103 107
s
I
J
I
1
v»8
This Volume is for
REFERENCE USE ONLY
K3
i
I
i
j§
I
1
I
I
I
l
I
1
L f/^lf/^lT/^lr7^1f7^lfy^ir7^lT/^lr?^if^^
ELECTRICAL ENGINEERS' HANDBOOK
Electric Communication
and Electronics
WILEY ENGINEERINGS HANDBOOK SERIES
OF ENGINEERING FUNDA-
MENTALS. Edited by OVID W. ESHBACBE.
KENT'S MECHANICAL ENGINEERS* HAND-
BOOK. Twelfth Edition.
DESIGN AND PRODUCTION. Edited by
COLIJN"
PO^VER. Edited by J. K.
ELECTRICAL ENOINEERS*
Fourth. Edition.
ELECTRIC POWER. Edited by
and WILLIAM: A. DEL
ELECTRIC COMMUNICATION AND
ELECTRONICS. Edited by HAJ^OLT*
and KLrsrox
ENGINEERS^ HANDBOOJEC.
Edition. Edited by tne late ROBERT PEELE.
HANI>KOOiC OF MIJNERAL ORESSKNTG.
ORES AND INDUSTRIAL MINERALS.
Edited by AetTHxna F.
ELECTRICAL
HANDBOOK
Electric Communication
and Electronics
Prepared by a Staff of Specialists
HAROLD FENDER, PH.D., Sc.D.
and
KNOX McILWAIN, B.S., E.E.
Editors
FOURTH EDITION
WILEY ENGINEERING
HANDBOOK SERIES
NEW YORK : JOHN WILEY & SONS, ING.
LONDON : CHAPMAN & HALL, LIMITED
COPYRIGHT 1914, 1922, 1936, 195O
BY
JOHGNT "WlLEY & SoisTS, IlSTC-
Copyright 1914 renewed, 1941
Copyright 1922 renewed, 1949
3By John. Wiley & Sons, Inc.
Copyright, Canada, 1936, 195O; International Copyright, 1936, 195O
John Wiley & Sons, Inc., Proprietors
Rights Reserved
fta l>ook or curby yya,rt thereof must not
be reproduced, 'in any form,
the written %>ermi>&afion of the
PRI3STTED I3ST THE UNITED STATES OF AI^ERICA
PREFACE
The first edition of Fender's Handbook for Electrical Engineers, compiled by a staff of
specialists under the editorship of Harold Fender, appeared in 1914. The second edition,
under the joint editorship of Fender and William A. Del Mar, was published in 1922-
Both these editions covered all branches of electrical engineering as well as a large amount
of material dealing with allied fields of interest to electrical engineers.
The third edition, published in 1936, was divided into two volumes: one on electric
power under the editorship of Fender, Del Mar, and Knox Mcllwain; the other on elec-
trical communication and electronics under the editorship of Fender and Mcllwain.
Certain tables and fundamental theory were duplicated in the two volumes in order that
each might be complete and independent of the other.
This plan met with such enthusiastic response that it has been continued in the fourth
edition. The growth of knowledge and the greater degree of specialization in the various
phases of electrical engineering have necessitated a considerable enlargement of both
volumes. Careful selection and Compression have been exercised in an effort to keep
the books compact and readable. The treatment of subjects of decreased importance
and those which are adequately treated by other handbooks of the Wiley Handbook
Series has been either curtailed or left unchanged in length.
The bibliographies have been prepared with the idea of assisting the reader to further
study of each subject-, and they reflect each author's idea of this plan. The publications
referred to are, in general, in the Engineering Societies Library, 29 West 39th Street,
New York, N. Y. Most of them may be borrowed from the Library by members of its
Founder Societies, the American Society of Civil Engineers, American Institute of Mining
and Metallurgical Engineers, American Society of Mechanical Engineers, and American
Institute of Electrical Engineers.
Seventy-eight specialists in their respective fields have contributed to this fourth and
entirely rewritten edition of the, Electronics and Communication portion of the Electrical
Engineers1 Handbook, as compared with twenty-seven, forty-five, and fifty-seven in pre-
vious editions. This reflects the rapid widening in the electronics field. In particular,
frequency modulation and all the pulse techniques in both the communication and radar
fields appear in the volume for the first time. The increased complexity and importance
of radio aids to navigation are also of interest.
The editors' thanks are due to the many well-known and busy men who have con-
tributed textual material, both for their unselfish efforts to make this a reliable reference
work and for their continued patience with editorial vagaries. They are also due to
Messrs. R. L. Jones, R. K. Honaman, and A. R, Thompson of the Bell Telephone Labora-
tories, Mr. Frank A. Cowan of the American Telephone and Telegraph Company, and
Mr. E. W. Engstrom of RCA Laboratories for aid in the organization of the book.
HAEOLD FENDER
KNOX MclLWAIN
LIST OF CONTRIBUTORS
Maurice Artzt, Research Engineer, Radio Corp. of America, RCA Laboratories Divi-
sion. Facsimile.
W. F. Bailey, Sr. Television Engineer, Hazeltine Electronics Corp. Television Receivers.
^ Loy E. Barton, Research Engineer, Radio Corp. of America, RCA Laboratories Divi-
sion. Amplifiers.
Dr. R. M. Bozorth, Research Physicist, Bell Telephone Laboratories. Magnetic Mate-
rials.
Dr. J. G. Brainerd, Professor, Moore School of Electrical Engineering, University of
Pennsylvania. Units and Conversion Factors, Symbols and Abbreviations.
R. B. J. Bnmn, Sr. Engineer, Hazeltine Electronics Corp. Television Receivers.
T. J. Buzalski, Television Station Engineer, National Broadcasting Company. Tele-
vision Broadcasting.
Dr. Carl C. Chambers, Acting Dean, Moore School of Electrical Engineering, Uni-
versity of Pennsylvania. Mathematics, Mathematical Tables, Units and Conversion Fac-
tors, Symbols and Abbreviations, Constants, Oscillators.
R. A. Chegwidden, Member of Technical Staff, BelHTelephone Laboratories. Magnetic
Materials.
H. A. Chinn, Chief Audio Engineer, Columbia Broadcasting System. Audio Facilities
for Sound Systems, Radio Telephone Broadcasting.
E. L. Clark, Sr. Television Engineer, Radio Corp. of America, RCA Victor Division.
Special Purpose Amplifiers.
James I. Cornell, Vickers Electric Division, Vickers, Inc. Capacitors, Condensers.
L. F. Curtis, Consultant, Hazeltine Electronics Corp. F-m Receivers.
B. J. Dalton, Industrial Engineering Division, Apparatus Dept., General Electric Com-
pany. Electronic Control Equipment.
Paul S. Darnell, Transmission Apparatus Engineer, Bell Telephone Laboratories. Re-
sistors and Rheostats.
Howard L. Davis, Jr., Engineer in Charge, Special Investigation Section, Engineering
Department, Philadelphia Electric Company. Coordination of Communication and Power
Systems.
William R. Dohan, General Consultant, Consulting and Standards Division, Engineer-
ing Dept., Radio Corp. of America, RCA Victor Division. Insulating Materials.
R. D. Duncan, Jr., Engineering Consultant. F-m Systems.
Dr. D. W. Epstein, Research Engineer, Radio Corp. of America, RCA Laboratories
Division. Geometrical Optics, Electron Optics.
J. G. Ferguson, Engineer, Bell Telephone Laboratories. Measurement of Primary Elec-
trical Quantities.
J. L. Finch, Plant Design Superintendent, Radio Corp. of America, RCA Communica-
tions, Inc. Radio Telegraph Systems.
H. J. Fisher, Test Engineer, Bell Telephone Laboratories. Wire Line Measurements.
F. J. Gaffney, Chief Engineer, Polytechnic Research and Development Co., Inc. Signal
Generators and Power Measurements.
Dr. Maxwell K. Goldstein, Air Navigation Development Board, CAA, Dept. of Com-
merce. Radio Aids to Marine Navigation.
A. J. Grossman, Member of Technical Staff, Bell Telephone Laboratories. Electric
Wave Filters.
0. B. Gunby, Recording Equipment Systems Engineer, Radio Corp. of America, RCA
Victor Division. Sound Recording.
A. L. Hammerschmidt, Development Engineer, National Broadcasting Company, Tele-
vision Broadcasting.
W. B, Hebenstreit, Section Head, Navigation and Radar Research, Electronics De-
partment, Hughes Aircraft Company; formerly with Bell Telephone Laboratories. Mag-
H. A. Henning, Member of Technical Staff, Bell Telephone Laboratories. Magnetic
Recording and Reproducing of Sound, Mechanical Recording and Reproducing of Sound.
L. M. Hershey, Director of Research, General Instrument Corporation. Inductors with
Air Cores.
Vlll LIST OF CONTRIBUTORS
C. J. Hirsch, Chief Engineer, Research Division, Hazeltine Electronics Corp. /-/
Amplifier a.
E. W. Houghton, Engineer, Bell Telephone Laboratories. Microwave Measurements.
Dr. Herbert E. Ives, Research Consultant, Bell Telephone Laboratories. Photorespon-
sive Devices.
A. P. Kauzmann, Engineer, Vacuum Tube Advanced Development, Radio Corp. of
America, RCA Victor Division. Thermionic Vacuum Tubes.
C. R. Keith, Engineering Representative, ERP Division, Western Electric Company.
Photographic Sound Recording.
J. P. Kinzer, Member of the Technical Staff, Bell Telephone Laboratories. Canty
Resonators.
Hugh S. Knowles, Vice President, Jensen Manufacturing Company, President Indus-
trial Research Products, Inc. Effects of tfie Acoustic Medium, Loudspeakers and Telephone
Receivers, Microphones.
Vern O. Knudson, Dean and Professor of Physics, Graduate Division, University of
California. Acoustic Properties of Rooms, Sound Insulation, Acoustic Design of Auditoriums.
R. J. Kowalski, Commercial Engineer, Custom Built Dept., Radio Corp. of America,
RCA Victor Division. Electro-acoustic Equipment, Public-address Systems.
V. D. Landon, Radio Research Engineer, Radio Corp. of America, RCA Laboratories
Division. Single Mesh and Coupled Circuits, Detectors, Radio Receivers.
H. W. I/everenz, Research Chomico-Physicist, Radio Corp. of America, RCA Labora-
tories Division. Luminescent and Tenebrescent Materials.
B. D. Loughlin, Sr. Engineer, Hazeltine Electronics Corp. Distortion and Interference
in F-m Systems.
A. V. Loughren, Vice President in Charge of Research, Hazeltine Electronics Corp.
Television Principles and Theory.
Warren A. Harrison, Member of Technical Staff, Bell Telephone Laboratories. Fre-
quency Measurements.
Dr. Warren P. Mason, Research Physicist, Bell Telephone Laboratories. Piezoelectric
Crystals.
Knox Mcllwain, Chief Consulting Engineer, Hazeltine Electronics Corp. Non-linear
Electric Circuits, Electromagnetic Radiation, Electromechanical Systems, Conducting Mate-
rials, Single Mesh and Coupled Circuits.
Henry I. Metz, Chief, Electronics Maintenance Branch, Maintenance Engineering Div.,
Civil Aeronautics Administration. Radio Aids to Air Navigation.
H, F. Mickel, Communication Sales Manager, Raymond Rosen Engineering Products,
Inc. Police Radio.
W. A. Munson, Telephone Engineer, Bell Telephone Laboratories. The Sense of Hear-
ing, Speech and Music, Effect of Distortion.
Dr. Kenneth N. Ogle, Optical Research Dept., Mayo Clinic. Vision.
J. J. Okrent, Sr. Engineer, Hazeltine Electronics Corp. Pulse Circuits.
D. S. Peck, Member Technical Staff, Bell Telephone Laboratories. Gaseous Conduc-
tion Tubes.
Harold Pender, Consultant, Moore School of Electrical Engineering, University of
Pennsylvania.
Dr. E. Peterson, Member Technical Staff, Bell Telephone Laboratories. Wave Analysis.
J. D. Phyfe, Product Engineer, Theatre Sound Equipment, Radio Corp. of America,
RCA Victor Division. Projection Practices.
N. Y. Priessman, Member of Technical Staff, Bell Telephone Laboratories. Varistors
and Thermistors.
Dr. G. L. Ragan, Research Associate, General Electric Company. Wave-guide Compo-
nents.
Dr. E. G. Ramberg, Research Physicist, Radio Corp. of America, RCA Laboratories
Division. Television Pick-up Tubes.
P. H. Richardson, Member of Technical Staff, Bell Telephone Laboratories. Theory of
Linear Passive Networks, Recurrent Networks.
Arnold J. Rohner, Project Engineer, Bendix Radio Division. Ferrous Cored Inductors,
Transformers with Iron Cores.
A. L. Samuel, Professor of Electrical Engineering, University of Illinois. Klystrons.
Arthur H. Schafer, Member of Technical Staff, Bell Telephone Laboratories. Resistors
and Rheostats.
Dr. S. A. Schelkunoff, Member of Technical Staff, Bell Telephone Laboratories. Wave-
guide Theory.
J. C. Schelleng, Radio Research Engineer, Bell Telephone Laboratories. Radio An-
tennas, Transmission in Space.
LIST OF CONTRIBUTORS IX
Dr. Theodore Seller, Professor of Physics, Amherst College. Cathode-ray Tube Displays,
F. J. Somers, Staff Engineer, National Broadcasting Company. Television Broadcasting*
Dr. John C. Steinberg, Member of Technical Staff, Bell Telephone Laboratories. The
Sense of Hearing, Speech and Music, Effects of Distortion.
L. E. Swedlund, Sr. Engineer, Radio Corp. of America, RCA Victor Division. Cathode-
ray Tubes.
W. O. Swinyard, Chief Engineer, Hazeltine Research, Inc. Routine Measurement of
A-m and F-m Broadcast Receivers.
John D. Taylor, Consulting Engineer, American Telephone & Telegraph Company.
Telephony, Telegraphy, Coordination of Communication and Power Systems, Wire Trans-
mission Lines, Mechanical Features of Transmission Lines.
L. Vieth, Member of Technical Staff, Bell Telephone Laboratories. Magnetic Recording
and Reproducing of Sound, Mechanical Recording and Reproducing of Sound.
Arthur H. Volz, Member of Technical Staff, Bell Telephone Laboratories. Potentiom-
eters and Rheostats.
Dr. S. Reid Warren, Jr., Associate Professor, Moore School of Electrical Engineering,
Associate Professor Radiologic Physics, Graduate School of Medicine, University of Penn-
sylvania. X-ray Tubes, Medical Applications of Electricity.
Charles Weyl, Professor, Moore School of Electrical Engineering, Associate Professor
of Radiologic Physics, Graduate School of Medicine, University of Pennsylvania. Med-
ical Applications of Electricity.
H. A. Wheeler, Consulting Radio Physicist, engaged for this work by Hazeltine Elec-
tronics Corp. Pulse Techniques, Transient Networks.
I. G. Wilson, Member of Technical Staff, Bell Telephone Laboratories. Cavity Reso-
nators.
J. E. Young, Supervisor, Broadcast Engineering Section, Radio Corp. of America, RCA
Victor Division. Modulators, Power Supply, Radio Transmitters, F-m Transmitters.
Dr. V. K. Zworykin, Vice President and Technical Consultant, Radio Corp. of America,
RCA Laboratories Division. Television Pick-up^Tubes.
GENERAL TABLE OF CONTENTS
Detailed tables of contents are given at the beginning of each section. An alphabetical index appears
after Section SS.
SECTION 1. MATHEMATICS, UNITS,
AND SYMBOLS
PAGE
Mathematics , 1-02
Mathematical Tables and Charts 1-19
Units and Conversion Factors 1-42
Symbols and Abbreviations 1-71
Constants 1-79
SECTION 2. PROPERTIES OF MATERIALS
Conducting Materials .
Insulating Materials . .
Magnetic Materials . , ,
2-02
2-21
2-56
SECTION 3. RESISTORS, INDUCTORS,
AND CAPACITORS
Resistors and Rheostats . . .
Varistors and Thermistors.
Inductors with Air Cores . .
Ferrous-cored Inductors . . .
Capacitors
3-02
3-22
3-31
3-42
3-53
SECTION 4. ELECTRON TUBES
Thermionic Vacuum Tubes .
Magnetrons
Klystrons
Gaseous Conduction Tubes .
X-ray Tubes
4-02
4-40
4-51
4-58
4-81
SECTION 6. ELECTRIC CIRCUITS,
LINES, AND FIELDS
Theory of Linear Passive Networks .... 5-02
Recurrent Networks 5-22
Transients in Networks 5-26
Non-linear Electric Circuits 5-37
Electromagnetic Radiation 5-49
Electromechanical Systems 5-56
SECTION 6. PASSIVE CIRCUIT ELEMENTS
Single-mesh and Coupled Circuits 6-02
Transformers with Iron Cores 6-13
Electric Wave Filters 6-33
Badio Antennas 6-62
SECTION 7. VACUUM-TUBE CIRCUIT
ELEMENTS
Amplifiers 7-02
Special-purpose Amplifiers 7-31
Intermediate-frequency (I-F) Amplifiers 7-56
Modulators 7-70
Detectors 7-76
Oscillators 7-83
Power Supply 7-106
Radio Receivers 7-115
Radio Transmitters 7-128
SECTION 8. FREQUENCY MODULATION
Frequency-modulation Systems 8-02
Frequency-modulation Transmitters 8-09
Frequency-modulation Receivers 8-16
Distortion and Interference in F-M Sys-
tems 8-26
SECTION 9. PULSE TECHNIQUES
Pulses and Pulse Systems.
Pulse Circuits '.
PAGE
9-02
9-13
SECTION 10. TRANSMISSION CIRCUITS
Wire Transmission Lines 10-02
Wave Guides— Theory 10-09
Wave-guide Components 10-17
Transmission in Space 10-29
Mechanical Features of Transmission
Lines 10-49
Coordination of Communication and
Power Systems 10-67,
SECTION 11. ELECTRICAL
MEASUREMENTS
Frequency Measurements 11-02,
Measurement of Primary Electrical
Quantities 11-16
Wire Line Measurement 11-32
Routine Measurements on A-M and F-M
Broadcast Receivers 11-43
Wave Analysis 11-54
Microwave Measurements 11-69
Signal Generators and Power Measure-
ment 11-89
SECTION 12. ACOUSTICS
The Sense of Hearing 12-02
Speech and Muaic 12-19
Effects of Distortion on Speech and Music 12-29
Acoustic Properties of Rooms 12-39
Sound Insulation 12-57
Acoustic Design of Auditoriums 12-69
SECTION 13. ELECTROMECHANICAL-
ACOUSTIC DEVICES
Effects of the Acoustic Medium 13-02
Loudspeakers and Telephone Receivers . 13-08
Microphones 13-22
Magnetic Recording and Reproducing of
Sound 13-28
Mechanical Recording and Reproducing
of Sound 13-37
Photographic Sound Recording 13-47
Piezoelectric Crystals 13-55
SECTION 14. OPTICS
Geometrical Optics 14-02
Vision 14-25
Electron Optics 14-49
SECTION 15. ELECTRO-OPTICAL
DEVICES
Photoresponsive Devices 15-02
Television Pick-up Tubes 15-19
Luminescent and Tenebrescent Materials 15-29
Cathode-ray Tubes 15-41
Xil
GENERAL TABLE OF CONTENTS
SECTION 16. SOUND-REPRODUCTION
SYSTEMS
PAGE
Audio Facilities for Sound Systems 16-02
Electroacoustic Equipment 16-11
Public-address Systems 16-14
Sound Recording and Projection 16-19
Radio Telephone Broadcasting 16-25
Police Radio 16-35
SECTION 17. TELEPHONY
Central-office Equipment 17-03
Radio Telephone Systems 17-54
Telephone Lines — Transmission Consid-
erations 17-69
Program Service 17-101
Subscriber Stations 17-106
SECTION 18. TELEGRAPHY
Theory 18-02
Telegraph Systems 18-18
Submarine Cable Telegraphy 18-40
Telegraph Equipment 18-46
Transmission Maintenance 18-53
Radio Telegraph Systems 18-56
SECTION 19. FACSIMILE TRANSMISSION
AND RECEPTION
Scanning Systems 19-02
Recording Systems 19-11
Synchronizing and Phasing 19-18
Transmission Characteristics 19-22
Specialized Applications 19-23
SECTION 20. TELEVISION
PAGE
Principles and Theory 20-02
Television Broadcasting 20-21
Television Receivers 20-46
Other Forms of Television 20-64
SECTION 21. ELECTRONIC CONTROL
EQUIPMENT
Fundamental Electronic Power Circuits 21-02
Fundamental Electronic Control Circuits 21-13
Complete Electronic Devices 21-20
SECTION 22. AIDS TO NAVIGATION
Radio Aids to Air Navigation 22-04
Radio Aids to Marine Navigation 22-33
SECTION 23. MEDICAL APPLICATIONS
OF ELECTRICITY
Electrotherapy and Shock Therapy .... 23-02
Diathermy and High-frequency Surgery 23-04
The Medical Uses of Ultraviolet and In-
frared Radiations 23-06
Electrocardiography and Electroenceph-
alography 23-08
Electroacoustic Devices 23-11
Roentgen Therapy 23-12
Roentgenography and Roentgenoscopy . 23-14
High- voltage Shock and X-ray Burn . . . 23-17
Tills book Is divided into sections, each section
carrying its in. dependent seqnen.ce of page numbers.
For example, 3— 315 in.dica.tes Section 3, page ±5.
SECTION 1
MATHEMATICS, UNITS, AND SYMBOLS
MATHEMATICS
ART. BY CARL C. CHAMBERS PAGE
1. Algebraic Formulas 02
2. Complex Quantities 06
3. Trigonometric Formulas 07
4. Exponential and Hyperbolic Formulas. . 10
5. Calculus Formulas 12
6. Differential Equations 13
7. Errors of Observation 15
8. Approximations 16
9* Series 17
10. Mensuration 17
MATHEMATICAL TABLES AND CHARTS
11. Common and Natural Logarithms of
Numbers 19
12. Trigonometric Tables 21
13. Exponential and Hyperbolic Tables .... 26
14. Bessel Functions 37
15. Transmission Unit and Power Reference
Levels. — Decibels 37
UNITS AND CONVERSION FACTORS
BY J. G. BRAINERD AND CARL C. CHAMBERS
16. Systems of Units 42
17. Conversion Tables 47
Table
1. Length (L) 47
2. Area (L2) 48
3. Volume (L3) 49
4. Plane Angle (No Dimensions') . . 51
5. Solid Angle (No Dimensions) . . 51
6. Time (T) 51
7. Linear Velocity (LT~l) 52
8. Angular Velocity (T~l) 53
9. Linear Acceleration (LT~2) ... 53
10. Angular Acceleration (T7""2) 53
11. Mass (M) and Weight 54
12. Density or Mass per Unit Vol-
ume (,MX~3) 55
13. Force (MLT~2) or (F) 55
14. Torque or Moment of Force
(ML2T~2) or (FL) 56
15. Pressure or Force per Unit Area
(ML-1T~2) or (FL~2) 56
16. Energy, Work and Heat
(ML2T~2) or (FL) 57
17. Power or Rate of Doing Work
(ML2T~*) or (FLT~l) 58
18. Quantity of Electricity and
Electric Flux (Q) 58
Table
19.
20.
21.
22.
23.
24.
25.
26.
27.
28.
29.
30.
31.
32.
35.
18. Gages.
Charge per Unit Area and
Electric Flux Density (QI/~2) 59
Electric Current (QT~l) ....... 59
Current Density (QT~1L~2) , . . 59
Electric Potential and Electro-
motive Force (MQ~1L2T~2)
~
Electric Field Intensity and Po-
tential Gradient (MQ^LT'2)
or (FQ-1) .................
Electric Resistance
(MQ~2L2T~^ or (FQ~2LT) .
Electric Resistivity
(MQ~WT~l) or (FQ~2L2T)
Electric Conductivity
(M-1Q2L~3T)
(F~1Q2L-*
Capacitance
--
Inductance (MQ~2L2) or
(FQ~2LT2) ................
Magnetic Flux (MQ^L2^1} or
Magnetic Flux Density
(MQ-iT-1) or (FQ~1L~1T) .
Magnetic Potential and Mag-
netomotive Force (QT~l)
Magnetic Field Intensity, Po-
tential Gradient, andJVtagne-
tizing Force (QL~~1T~1')
Specific Heat (L2T~2t~
60
60
61
61
62
62
63
63
63
64
64
64
Thermal Conductivity
(MLT~zrl) and Thermal Re-
sistivity (Af"~1zr~1:r3i) (t =
Temperature) 65
Light 65
66
SYMBOLS AND ABBREVIATIONS
19. Abbreviations for Engineering Terms. . . 71
20. Letter Symbols for the Magnitudes of
Electrical Quantities 72
21. Standard Graphical Symbols 76
22. Use of Greek Alphabet for Symbols 79
CONSTANTS
BY CARE, C. CHAMBERS
23. Principal Physical Constants and Ratios 79
24. Standard Radio-frequency Ranges 80
1-01
MATHEMATICS, UNITS, AND SYMBOLS
MATHEMATICS
By Carl C. Chambers
1. ALGEBRAIC FORMULAS
MISCELLANEOUS FORMULAS
(a db&)2 - a2dh2a& + 62
(a d= 6)3 = a3 =b 3a2 6 + 3a62 db &3
(a =b b)n -2 feifrTife)! a* (±rfn~®* n! « »(n - 1) . . . 3 X 2 X 1
a2 - 62 « (a-f 6) (a- 6) _
a2 + 52 = (a -f y&)(0 -y&), y « V- i
a31 X ay = ate4v)f a° = 1 [for a 5* 0), (a&)* = a* 6*
- _
a" ' "a" \b
a1/*
log (a31) = a; log a, log #& = log a + log &
log 7 ^ log a — log 6
r£ a c a±6 c±d .a —
If 7 ~ - then — r — = — — and
~ — r — — — — r— - = — ; — _
b d b d a+b c + d
The sum of an arithmetical progression is given by
* = £(<* + *) -|{2a+(n- !)<*}
whore Z — a + (n — l)d is the last term, a is the first term, d is the common difference,
and « is tho sum of the n terms.
The sum of a geometrical progression is given by
(1 - rn) Ir - a
s — a — - = - -
1 — r r — 1
where Z » arn-1 is the last term, a is the first term, d is the common ratio, and s is the sum
of the n terms. If n approaches infinity and r2 is less than unity
The multiple product represented by n(n — l)(n — 2) . . . 3 X 2 X 1 is designated
by the symbol n! or |n and is called " n factorial." The following list gives the value of
n! up to n = 10
1! - 1 6! = 720
2! = 2 7! = 5,040
3! = 6 8! = 40,320
41 =24 9! « 362,880
5! - 120 10! = 3,628,800
1-02
ALGEBRAIC FORMULAS 1-03
For large values of n a good approximation for nl is, from Stirling's formula,
n\ = (2*7i) ** (-Y, e = 2.7182818
This formula is accurate to about 21f2 per cent at n = 10 and becomes more accurate
very rapidly as n is increased,
The number of permutations or arrangements of n things taken p at a time is
pn
*
The number of combinations of n things taken p at a time is then
QUADRATIC EQUATION. The solution of
ax2 + bx + c = 0
—6 db V&2 - 4ac
is re =
If a, &, and c are real, and the discriminant, 62 — 4ac, is positive, the roots are real and
unequal; if it is zero, the roots are real and equal; if it is negative, the roots are conjugate
complex numbers.
CUBIC EQUATIONS. The solution of
is obtained as follows:" Put x = - (y — 6) ; then (1) becomes
a
y3 - 3Hy + 0 = 0
where H = 62 — ac
G = a2 d - 3abc + 2bs
For a solution let
/?
then the values of y will be given by
1 Vs 1 Vs
y = A + B. — - (A + B) + j -r- (A — £), — - (A + B) — j (A — J?)
2222
If a, b, c, d are real and if (72 — 4F3, the discriminant, is positive there are one real
root and two conjugate complex roots; if G2 — 4#3 is zero there are three real roots, at
least two of which are equal; if (r2 — 4#3 is negative there are three real and unequal
roots.
The solution may be written in three other forms.
(1) Put
*-5«-
then the roots are
y = 2 VSsin 0, 2 V^T sin (0 + 120°), 2 v^sin (0 - 120°)
Or (2) put
le^rai
3 L2#v#J
then the roots are
y = — 2 V]j cosh w, ^~H cosh w + V— 3H sinh u, Vj? cosh u — V— 3# sinh u
Or (3) put
1 . ,.r G
u = - smh 1 1 —
Then the roots are
^ = 2 V— H sinh w, — V— # sinh w + V§F cosh w
— V— ^ sinh w — VsH cosh w
SIMULTANEOUS EQUATIONS. Given 7^ independent equations in n unknowns,
these n equations usually fix one or more values for each of the n unknowns. To solve
1-04
MATHEMATICS, UNITS, AND SYMBOLS
such, a set of simultaneous equations in x, y, and 2, say, solve each of the three equations
for x in terms of y and z. Equating these three values for x gives two equations in y
and z. Solving each of these two equations for y in terms of z and equating these two values
of y gives a single equation in z. The solution of this last equation then gives the value
of z. Then substitute this value of z in either of the equations in y and z, and solve for y.
Then substitute these values of y and z in any one of the original equations and solve for x.
DETERMINANTS. In the case of linear simultaneous equations (i.e., when x, y,
and z occur only to the first power), the equations may be solved by determinants. This
method is a considerable time-saver when the number of unknowns is greater than three,
but when the number of unknowns is three or less the straight substitution method is
preferable.
The determinant of a set of simultaneous equations is formed by writing the equations
one below the other with the same unknown in the same relative position in each. The
block of numbers forming the coefficients of the unknowns is called the determinant.
For example, the determinant of the equations
w +
to "h
w -f
w 4-
D
2/+ 2=6
y -f" 3z = 4
3y = 1
9 = 3
1111
1013
1230
1301
The values of any one of the unknowns, say y, is found by writing a second determinant,
Dy, exactly like the determinant D, except that the constants forming the right-hand
members of these equations are substituted for the coefficients of y in the determinant,
that is
1 6
Then
and similarly for the other unknowns.
The value of any determinant is found by making use of the following rules:
(1) If a determinant has two equal rows or columns, it is equal to zero.
(2) To any row or column one may add or subtract any number of times any other
row or column without altering the value of the determinant.
(3) To multiply any row or column by a number is the same as multiplying the
determinant by that number.
(4) If all the terms in a row or column except one are zero, the determinant reduces
to one of a lower order which may be obtained by striking out the row and column which
intersect at the element of the row or column which is not zero, and multiplying the whole
by that element, changing the sign of this element, however, if it is removed by an odd
number of elements from the principal diagonal. The principal diagonal is the line of
elements beginning at the upper left-hand corner and ending at the lower right-hand
corner. Thus,
the principal diagonal being that with the figures 1,4, 0, and 3. It is immaterial whether
the- distance from the diagonal is counted along a row or a column.
(5) The value of a determinant of the second order is
0,2 63
The reduction of determinants is effected by altering the terms according to the above
rules until a row or column is obtained in which all terms but one are zero. This enables
a reduction of order to be effected in accordance with rule 4. Reductions are continued
until one of the second order is obtained.
ALGEBRAIC FORMULAS
EQUATIONS OF COMMON CURVES. Straight Line.
y = x tan 6 -f- 6.
Circle.
Ellipse.
a2 &2
Parabola (Vertical).
y- fcz2
where k is a constant.
Parabola (Horizontal).
y « &V^
where & is a constant.
Hyperbola.
a2 2/2
"5 "~ 75 = 1 (Horizontal)
6 ^
Rectangular or Equilateral Hyperbola.
where ^ is a constant.
Catenary.
r cosh fca; —
where /c is a constant. The length of arc
from O to P is
«=» y sinh (kx)
fc
See tables of hyperbolic functions.
-rX
Sinusoid.
^Lsin (ax + 0).
,1-05
1-06 MATHEMATICS, UNITS, AND SYMBOLS
2. COMPLEX QUANTITIES
The square root of a negative quantity is called an " imaginary " quantity, or a pure
imaginary. A quantity consisting of the sum or difference of a real quantity and an
imaginary quantity is called a " complex " quantity. All the rules of ordinary algebra
apply to pure imaginaries and complex quantities. The square root of minus one is
called the imaginary unit and is usually represented by the symbol j (writers on pure
mathematics use the symbol i), that is,
Any complex quantity may then be written
a+jb
where a and 6 are both real quantities.
GEOMETRICAL REPRESENTATION OF A COMPLEX QUANTITY. A positive
real quantity may be represented by a line drawn on a plane in a given direction; a negative
real quantity may be represented by a line drawn in the opposite direction. Multiplying
a quantity by — 1 then reverses its direction. Also, since multiplying a real quantity by
v'— 1 twice is equivalent to multiplying it by — 1, the operation of multiplying once by
v— 1 may be represented by turning the line representing the quantity through 90°
in the positive direction of rotation. The positive direction of rotation is taken as the
opposite direction to that in which the hands of a clock move. Hence, a
complex quantity a + jb may be represented by the line OP in the
figure, where OA = a and AP = b. The complex quantity a + jb is
then completely specified by a line of length v a2 + bz making an angle
6, with the axis of reference OX where tan 0 = -, The length
a
f = Va2 -{•- 62 is called the magnitude of the complex quantity, and the angle
0 = tan""1 - is called its angle. From the figure it is evident that the complex quantity
a
a + jb may also be written
a + jb — M (cos 6 +j sin 0)
Expanding cow 0 and sin 0 into vSeries (see Series, Article 9) and adding, the resultant series
obtained is the series for e'e ; hence
a + jb - Me1'9 (1)
From the above definitions and equation (1) it is evident that complex numbers
possess the following properties:
ADDITION OF TWO COMPLEX QUANTITIES.
(a -f- jb) + (ai + jbi) = (a + ai) + /(& + &i)
SUBTRACTION OF TWO COMPLEX QUANTITIES.
(a + jb) — (ai + jbi) = (a — ai) + j(b — 61)
MULTIPLICATION OF A COMPLEX QUANTITY BY A COMPLEX NUMBER.
(a + jb) (ai + jbi) — aai — bbi + j(abi + a\ 6)
or, putting a + ft = Me1'9 and en + jbi = Mi e^1
whore M =
and tan 0i = —
ai
we have (a + jb) (01 + ybi) = M49 Ml </dl - Jlf MI
Honco the product of two complex quantities is in general a complex quantity which has
a magnitude equal to the product of the magnitudes of the two quantities and an angle
equal to tho sum of the angles of the two quantities.
DIVISION OF A COMPLEX QUANTITY BY A COMPLEX NUMBER.
a + Jb _ (a + ;'?>) (ai — y&i) _ aai + bbi — y(abi — ai b)
"" i) (ai — fti) ~" ^ + &i2
M3Q M_ j(e- 6i)
Mi<Jdl==S Mi
TEIGONOMETRIC FORMULAS
1-07
Hence the quotient of two complex quantities is in general a complex quantity which has a
magnitude equal to the quotient of the magnitudes of the two quantities and an angle
equal to the difference of the angles of the two quantities.
SQUARE ROOT OF A COMPLEX QUANTITY.
and in general
. /Va2 + 62 - a]
'V — i — J
a2 + fr2 + a . /Va2 + b2 -~a]
—2 >V 2 J
Hence the nth root of a complex quantity is, in general, a complex quantity which has
a magnitude equal to the nth root of the magnitude M of the quantity and an angle equal
one-nth of the angle of the quantity.
EQUATIONS CONTAINING COMPLEX QUANTITIES. Since a real quantity can-
not be equal to an imaginary quantity it follows that any equation of the form
A + JB - Ai + jBi
where A, B, A\, and Bi are all real quantities (which may, however, consist of any number
of terms) , is equivalent to the two equations
A = Ai
and
Also, if one member of an equation reduces to the form A -f- jB, then the other member of
this equation must likewise contain an equal real and an equal imaginary part.
See K. S. Johnson, Transmission Circuits for Telephonic Communication, D. Van Nos-
trand.
3. TRIGONOMETRIC FORMULAS
The trigonometric functions of an angle are the ratios to one another of the various
sides of a right triangle having the given angle as one of its angles. Kef erring to Fig. 1,
let B, P, and H be the three sides of a triangle. Then the trigonometric functions of the
angle x are
sine of x, abbreviated - sin x = ~
cosine of x, abbreviated cos x = —
tangent of re, abbreviated tan x — —
cotangent of x, abbreviated cot x = —
secant of x, abbreviated sec x = —
cosecant of x, abbreviated esc x = —
When B, P, and H are limited to the three sides of a right triangle, the above definitions
are directly applicable only to angles lying between 0 and 90°. The definitions, however,
may be extended by considering the point A (Fig. 2) as describing a circle of radius OA
B „
FIG. 1
FIG. 2
with the center at 0. Let XX' be the horizontal diameter and YYf the vertical diameter
of this circle, and call P the perpendicular distance from A to the line XX' and B the
1-08
MATHEMATICS, UNITS, AND SYMBOLS
horizontal distance from A to YY'. P is to be considered positive when A lies above
XX', negative when below. B is considered positive when ,4 is to the right of FF7 and
negative when to the left. The four quarters of the circle are called quadrants, and are
designated as the first, second, third, and fourth quadrants as indicated. The angle is
said to lie in the quadrant in which the point A lies. In Fig. 2 the angle x is in the second
quadrant.
Algebraic Signs of the Functions
Sine
Cosine
Tangent
Angle in first quadrant
+
+
+
Angle in second quadrant
+
Angle in third quadrant
_
+
Angle in fourth quadrant
-
+
Period. From the above definitions it is evident that adding 2?r radians or 360° to an
angle does not change the value of any of its functions; that is, these functions repeat
themselves every time the angle increases by the 2ir radians or 360°. They are therefore
said to have a period equal to 2ir radians or 360°.
Functions of Angles in Any Quadrant in Terms of Angles in First Quadrant.
sin (90 + #) = cos x
cos (90 + re) = — sin x
tan (90 + x) = - cot x
sin (180 4- re) - — sin x
cos (180 -f x] = —coax
tan (180 + x) = tan x
sin (270 + a;) == — cos x
cos (270 -f- re) = sin x
tan (270 + x] = - cot x
sin ( — x) — — sin x
cos ( — re) — cos x
tan ( — x] = — tan x
sin (180 — x) — sin x
cos (ISO — x] — — cos x
tan (180 - x) = - tan x
sin (270 — x) = — cos x
cos (270 - x) - — sin x
tan (270 - x) = cot x
Anti-functions. If a = sin x, then x is the angle whose sine is a; this may be expressed
symbolically x = sin"1 a, which is read "x equals the angle whose sine is a." The angle x
is also called the "anti-sine" or the "inverse sine" of a. Similar notation is used for the
other functions; for example, x — cos™1 b is used to express the relation that x is the angle
whose cosine is b. At least two "anti-functions" must be known to completely determine
the quadrant in which an angle lies; for example, if x — sin""1 0.5 then x may be either 30°
or 150°, but if we also have x = cos"1 0.866, then x must equal 30°, while if x - cos"1
(-0.866), then re must equal 150°.
Anti-functions may be taken from the Trigonometric Tables by finding the angle in the
margin corresponding to the function in the table.
Example, sin"1 0.319 « 18.6° or 180° - 18.6° = 161.4°.
Versine. The expression (1 — cos x) is called the "versine" of x.
Relations among Functions of the Same Angle.
x sin x
1
cos re
- sin re 4~ cos re —
cot x
1
11 +01-»2 n.
1
sec re — "
cosrr
T tan'5 re —
cos2 re
1
1
esc re — • • • • .
sin x
1 4" cot re —
sin2 re
sin (90 — re) = cos re
sin (-re) =
— sin re
cos (90 — re) = sin re
cos ( — re) =
cos re
tan (90 — re) = cot x
tan ( — re) =
— tan re
Sum and Difference of Two Angles
sin (re 4- 2/)
= sin re cos y 4- cos re sin y
cos (x 4- y)
— cos re cos y — sin re sin y
tan (re 4- y)
tan x 4- tan y
1 — tan re tan y
sin (re — y)
= sin re cos y — cos re sin y
cos (x — y}
— cos x cos y 4" sin re sin y
tan re — tan y
tan (x y)
1 4- tan re tan y
TRIGONOMETRIC FORMULAS
1-09
Product of the Functions of Two Angles.
sin x sin y = 1/2 [cos (x — y) — cos (x + y}]
sin x cos y = 1/2 [sin (a; + 2/) + sin (x — y}]
cos £ sin y = 1/2 [sin (# + y) — sin (a: — y)]
cos re cos y — 1/2 [cos (x + y) + cos (a; — y)]
Functions of Twice an Angle.
sin 2x = 2 sin # cos a; cos 2:c = cos2 x — sin2 x = 2 cos2 a; — 1
2 tans;
tan 2iX •
Functions of Half an Angle.
I — cos x
1 - tan2 x
Functions of Three Times an Angle.
sin 3x = 3 sin x — 4 sin3 x cos 3rc = 4 cos3 x — 3 cos x
3 tan x — tan3 x
tan 3# =5
1-3 tan2 x
TRIGONOMETRY. Any triangle is completely denned when FIG. 3
(1) two sides and the included angle are known, (2) one side and two
angles are known, (3) three sides are known. Let the sides and angles of a triangle be
designated as in Fig. 3.
1. Given two sides a and &, and the included angle -y. Then
c = Va2 + 62 — 2 ab cos 7
a .
- sin 7
c
0 « 180 - a - T
2. Given the side a and the two angles (3 and 7. Then
a = 180 - 0 - 7
c — a •
sm a
sin 7
sin OL
3. Given the three sides a, &, and c. Put
s = V2 (a + b + c)
Then
sin
= r- Vs(s — a)(s —
6c
sin |8 — - sin a
a
— c)
•y - 180 - a - 0
Relations between Sides and Angles. The following relations between the sides and
angles of a triangle are sometimes useful :
b
a
sin a
c
sin 7
26c
and similar relations for the other two angles.
1-10 MATHEMATICS, UNITS, AND SYMBOLS
4. EXPONENTIAL AND HYPERBOLIC FORMULAS
When the relation between any variable y and another variable x is such that x occurs
as an exponent of one or more terms, y is said to be an exponential function of x. Of
particular importance in connection with electric circuits are the exponential functions
ex and e~x, where e is the base of the natural logarithms. Since x is the natural logarithm
of ex, the value of ex can be obtained from the table of common logarithms as shown at the
beginning of that table. In addition the values of ex and e~x are given in a separate table.
Hyperbolic functions are an extension of the trigonometric functions to those cases
where the use of the latter gives rise to imaginary or complex angles. From the relations
e** - e-**
sin x — : •
where j = v — 1, it follows that, putting x — jz:
e* -f e~~* ,
COSJZ = (1)
—j sin jz = (2)
Expressions (1) and (2) are both real quantities when z is real, that is, when the angle jz
is imaginary. The first expression is called the hyperbolic cosine of z, abbreviated and
pronounced "cosh"; the second expression is called the hyperbolic sine of z, abbreviated
sinh and pronounced "shin." Hence, using x for the variable,
sinh x
cosh x —
2
The hyperbolic tangent, cotangent, secant, and cosecant are defined as follows:
sinh x
tanh x
coth x =
sech x =
csch x —
cosh a;
cosh x
sinh x
1
sinh x
The hyperbolic angle a; is a number analogous to radians in circular measure; it is never
expressed in degrees.
Adding 2-Tr to an angle does not change the value of the trigonometric functions; they
are therefore said to have a period equal to 2?r radians. Hyperbolic functions, however,
have no true period, but adding 2trj to the hyperbolic angle does not change the values
of the functions; hence these functions have an imaginary period, 2wj.
For the value of the hyperbolic functions see tables of exponential and hyperbolic
functions, Article 13.
Approximate Formulas. Note that, for x less than 0.1,
sinh x = x with an error of less than 0.2 per cent
cosh x ** 1 -f — with an error of less than 0.09 per cent
£
For x greater than 6,
ex 1
sinh x = cosh x = — • — - logic"1 (0.43429#)
2i 2i
with an error of less than 0.01 per cent.
Anti-functions. If a — sinh x, then x is the angle whose hyperbolic sine is a; this may
be expressed symbolically
x = sinh"1 a
which is read "x equals the angle whose hyperbolic sine is a." The angle x is also called
the "anti-hyperbolic sine" or the "inverse hyperbolic sine." of a. Similarly for the other
EXPONENTIAL AND HYPEEBOLIC FORMULAS 1-11
hyperbolic functions. The following relations exist between the anti-hyperbolic functions
and the natural logarithms:
sinh"""1 x = log (x -f Vrc2 + 1 )
cosh"1 x = log (x + Vrc2 — 1 )
tanh"1 x — - log
Relations among Functions of the Same Angle.
cosh2 x — sinh2 x — 1
i
1 — tanh2 re =
coth2 x - I =
cosh2 x
1
sinh2 re
sinh ( — x) = — sinh x
cosh ( — x) — cosh x
tanh ( — x) = — tanh re
See also the definitions given above.
Sum and Difference of Two Angles..
sinh (x + y) — sinh re cosh y + cosh re sinh y
cosh (re -j- 2/) = cosh x cosh y + sinh re sinh y
. . , . tanh re -f- tanh y
tanh (re ~r y) —
1 + tanh x tanh y
sinh (x — y) — sinh x cosh y — cosh x sinh y
cosh (re — y} ~ cosh re cosh y — sinh re sinh y
, . . N tanh x — tanh y
tanh (x — y) - — - — - — —
1 — tanh x tanh y
Product of the Functions of Two Angles.
sinh x sinh y = 1/2 [cosh (x + y) — cosh (re — y}]
sinh re cosh y = 1/2 [sinh (re + y) -f- sinh (re — y)]
cosh re sinh y = 1/2 [sinh (re + 2/) — sinh (re — 2/)]
cosh re cosh y — 1/2 [cosh (# + 2/) -f- cosh (re — y)]
Functions of Twice an Angle.
sinh 2x ~ 2 sinh re cosh re
cosh 2x = sinh2 re + cosh2 re « 2 sinh2 re + 1 =* 2 cosh2 re - 1
. rt 2 tanh x
tanh 2:c = - — -— — r-r-
1 + tantr x
Functions of Half an Angle.
. ^ ^ /cosh re — 1
Sinn — —
x ^ /cosh re •
2
x
2 V Cosh re + 1
Functions of Three Times an Angle.
sinh 3rc = 3 sinh re -f- 4 sinh3 re
cosh 3x = 4 cosh3 # — 3 cosh x
. ^ 3 tanh x + tanh3 re
tanh 3rc = — r^
1 + 3 tanh2 re
Relations between Hyperbolic and Trigonometric Functions.
sinh O'rc) = j sin re sin (jx) = y sinh a;
cosh (jx} — cos re cos (jx) — cosh re
tanh (jx) ~ j tan re tan (jx) — j tanh re
sinh^jrc = j sin"1 re sin"1^ == j sinh"1 re
tanh~xya; = j tan"1 re tan1"1^ = j tanh"1 x
j cos"1 jo; = log (re
1-12
MATHEMATICS, UNITS, AND SYMBOLS
Hyperbolic Functions of a Complex Angle.
sinh (x + jy] — sinh x cos y + j cosh x sin 3
M
-v
'cosh 2x — cos 2y
and tan 0 ••
2 tanhx
cosh (a; + jy] — cosh x cosy + j sinh re sin y —
where
where
where
where
5. CALCULUS FORMULAS
The formula for the integration by parts is:
/b j /»&
udv — [uv] — I vdu
a Ja
The following table is used in the formulas
#w _ al_^
tan 2;
N =
tanh (x
P =
A /cosh 2x +
jinx-tang/
rj-iii-
> 2
sinh
x cos y + y cosh x sin ?/
cosh x cos y 4- j sinh x sin j/
^ /cosh 2x —
cos 2;y j i j. i
I" sin 2y "j
^cosh 2x +
f «n>»~l
cos 2y
4. cos o;~l 1
ww ~. o-nrl R - - i-
Lsinh2xJ
2 tann 1 j_
jo ana z>2 — rt t
H- A2 J 2
'an [l- ^L2
^
/(a?) +
where C is an arbitrary constant.
/'(x)
/(*)
/'(*>
/W
1
1
1
X
m + 1 ^ .
cos2 ax
a
I
^
1
1
ax
a e ^
sin2 ax
a
,
1
1 y X
-,ax
mn -1 V 7i
a
Vaa + bx2
bx
1 6a.
1
1 _, ^/— 1
b log a ""
xVx2 + a
1 .
x
±-\/^2 _L. ,>.2
a
Va* ± x-
1
x
V~2 2
a
Vx2 - a2
_-_'L1 ~_
! .
dx dx
V
cosn ax
a
uz
U
sinh ax
- cosh ax
log x
x log x — x
a
tan ax
log (cos ax)
sin2x
— 1/a(cos x sin x — x)
a
taxxh ax
- log (cosh ax)
COS2X
1/2 (sin x cosx-}~ x)
a
DIFFERENTIAL EQUATIONS 1-13
MAXIMA AND MINIMA. Let y be any function of a variable re; then y will be a
maximum or minimum for any value of x which satisfies
(1)
u>u/
provided -r-^ is not zero. If the second derivative ~~ is positive for this value of x, then
the corresponding value of y is a minimum; if this second derivative is negative, the cor-
responding value of y is a maximum.
In case —^ is also zero for the value of x which satisfies (1), the corresponding value of
y is not a maximum or minimum unless -~ is also zero and — is not zero. When — — 0,
dx* dx* dx3
. . d*y . . . cfiy d*y
2/ is a minimum if — -. is positive and a maximum if — - is negative. In case — ; is also zero,
ax ax dx
similar relations must hold for the fifth and sixth derivatives, etc.
6. DIFFERENTIAL EQUATIONS
Differential equations of the following forms are met with in the theory of alternating
and transient currents.
The following notation is used: e = 2.7183- • • = base of natural system of logarithms;
x, y, z are variables. A, <j>, 7, and $ are constants of integration or arbitrary constants.
Other letters represent known constants.
Ay f\\
-— = ay (1)
dx '
Solution: y = Aeax
— -j- ay = 0 (2)
Solution: y = Ae~ax
^ + ay « b (3)
dx
Solution: y = - [1 — Ae~ax]
a
d2y
Solution: y = A sin (arc + <£)
-7-5 = a2?/ (5)
Solution: y = A sinh (ax + 4>)
Solution :
Case I. a2 positive: y — Ae~ux sin (ax + <£)
Case II. a2 negative: y = Ae~^x sinh (ax + <£)
Case III. a2 = 0: y = A(x + <^e-^x
--T •{• 2u- — h (M? + az)y — B sin (cox + 0) (7)
aar dx ,
The complete solution of this equation consists of the solution of (6) plus the term
I sin (ux + $ — 5) (a)
where 5 = tan"1 ""T -2
O T" W — W
For each additional sine term added to the right-hand member of the equation, there
will be a corresponding term of the same form as (a) in the solution.
(B sin 5\ .
I — J sm
\ 2ua> /
1-14 MATHEMATICS, TJNITS, AND SYMBOLS
B •*»<»* + «> (8)
Solution:
y = Aiemi* + A->em*x 4 • - • ^n^771** + •£# sin
where wii, W2, etc , are the n roots of the equation
mn 4- On-ittt71"1 4 ---- aim + OQ = 0
and JT and 5 are found by substituting the JTS sin (tax + 0 4 5) by itself in the given
differential equation and equating the coefficients of sin (ojrc + 6} and cos (W -f- 0)
respectively on the two sides of the resulting equation. When the second member of
the differential equation is a constant, B, the sine term in the solution becomes simply — .
Note that all the preceding equations are merely special cases of the general equation (8)
The complete solution of this equation contains an infinite number of terms of the form
y = e-(*-»)* [Aie™ sin (wx + nz + <£i) + A^e~mz sin (ux — nz + <#>2)] (a)
where Ai, <£i, A+, <fa, and two of the four constants «, s, m, and n are integration constants
(fixed by the terminal conditions). The values of m and n in terms of o> and s are
/-r ^ + e
in — cV ab cos — - —
2
. /-T . 17 4- e
n = c V ao sin — - —
where a = V(s + g)2 + co2, e = tan~J ( — ^— )
\« + «/
6 = V(s - e)2 + w2, 77 = tan
The values of co and s in terms of m and n are
VJ'G a + 0
__
where F « V(n + c^)2 + m2, a = tan"1
G = V(n - cg)2 4 m2, 0 = tan~i
n
The solution of eq. (9) may also be written as a series of terms of the form
y = Me~(u~*)x sin (ux 4 <£ 4 /u) (6)
•W = -p= Vcosh 2,(mz 4 7) 4 cos 2 (712 4 0)
tan /t = tanh (mz 4- 7) tan (nz 4 0)
where A, <$>, 7, and 0 are integration constants, and the relations between the other con-
stants 6>, s, m, and n are the same as above. *
In the special case when q = 0, the solution of eq. (9) is
y = fl-tw jy^ua; 4. n
where /i and/2 are any two arbitrary functions and u and n are connected by the relation
ERRORS OF OBSERVATION 1-15
= 0 (10)
This is known as Bessel's equation of order n. Jn(x), Bessel's function of the first kind of
order n, is a particular solution of this equation. It may be computed from the infinite
series :
xn f x2 ~4
J (x\ __ I 1 .._... L,
2nr(w -f 1) L 22(n + 1) 242!(n + l)(n + 2)
2*3Kn + !)(*'+ 2)(» + 3) +•
where T(n + 1) is the gamma function which reduces to unity for n = 0 and to nl for n
equal to any positive integer. In general, the function Jn(x) is an oscillatory function of
x having the value zero for x = 0, except for the case where n — 0. For values of n larger
than 1, the slope of Jn(x) is zero for x — 0 and the first maximum and the first zero occurs
at successively higher values of x as n takes on larger values. For small values of n, the
values of x for which Jn(x} is a maximum or zero can be gotten from tables of Bessel func-
tions. For large values of n, the first maximum, that is, the smallest x for which Jn'(x}
— 0, is given by
n + 0.809 v/n (b)
with an error not larger than l/^/n, and the first zero, that is, the smallest x for which
Jn(x) = 0, is given by
n -}- 1.856 -v/n (e)
again with an error of the order of l/\/n.
For integral values of n greater than zero,
2n
x
which permits one to compute Bessel functions for successively higher order from tables
of JQ(X) and Ji(x).
When n is an integer,
BIBLIOGRAPHY
Watson, G. N., A Treatise on the Theory of Bessel Functions, 2nd Ed., New York, The Macmillan Com-
pany (1944).
Article 14 of this section.
7. ERRORS OF OBSERVATION
When a quantity is measured with all possible accuracy many times in succession, the
numbers expressing the results are found to differ by amounts which, although generally
small, are occasionally considerable in comparison with the quantity measured. Though
these differences may be decreased by improved methods, better instruments, or greater
skill, they can never be entirely removed. They are known as the errors of observation.
The following formulas, which are derived from the theory of least squares, apply to such
errors and not to errors which can be eliminated by correcting mistakes of the observer or
defects of instruments or methods of observation. That is, they apply only to errors
which may be either positive or negative, the chance of a positive error occurring being
exactly the same as the chance of a negative error occurring.
WEIGHTED OBSERVATIONS. Sometimes, in spite of the care with which obser-
vations are taken, there are reasons for believing that some observations are better than
others. In this case the observations are given different "weights" or numbers express-
ing their relative practical worth. A weighted observation is an observation multiplied
by its weight.
PROBABLE VALUE OF SEVERAL OBSERVATIONS. The most probable value of
a quantity which is observed directly several times with equal care is the arithmetical
mean of the measurements.
The most probable value of a quantity which is observed directly several times, but
the observations of which have different weights, is equal to the sum of the weighted
observations divided by the sum of the weights.
1-16 MATHEMATICS, UNITS, AND SYMBOLS
PROBABLE ERROR OF ANY ONE OF SEVERAL OBSERVATIONS. The probable
error or dispersion of a number of direct observations made with equal care is given by
the following formula:
0.6745
* n — 1
where n = number of observations.
r - probable error of a single observation.
0 = residual found by subtracting the arithmetical mean from each measurement.
The probable error of each of a number of direct observations, where the observations
have different weight, is found by the following formula, in which p represents the per
unit weight of an observation.
0.6745
«n - 1
PROBABLE ERROR OF THE ARITHMETICAL MEAN. If
r = probable error of a single observation,
n = number of observations,
TQ = probable error of the arithmetical mean,
TQ = — — for observations of equal weight
Vn
or
Tt
: for unequal weight
It should be noted that the probable error of the mean decreases inversely as the square
root of the number of observations.
PROBABLE ERROR IN A RESULT CALCULATED FROM THE MEANS OF SEV-
ERAL OBSERVED QUANTITIES. Let Z « a sum or difference of several independent
quantities.
Let ri, 72, r3, etc., be the probable errors in these quantities. Then the probable error of
Z is equal to
Wi2 + r22 + r32 + etc.
Let Z — Az, where z is an, observed quantity, and A, a known number. Let r be the
probable error in z. Then the probable error in Z is Ar.
Let Z be the product of two independently observed quantities z\ and 22 whose probable
errors are r\ and r% respectively. Then the error in Z is equal to
4-
Let Z be any function of the independently observed quantities z\, zz, 23, etc., whose
probable errors are ri, r^ TZ, etc. Then the probable error in Z is equal to
8. APPROXIMATIONS
If a is small
(1 d= a) m = 1 ± ma
If mis nearly equal to n
m -f- n
If #, expressed in radians, is small compared to a radian
sin 0 = tan 8 = 6 radians
MENSURATION 1-17
9. SERIES
Taylor's series is written
f(x + K) = /(a» -f
where the prime on the function means the derivative with respect to the argument.
The following series are frequently useful.
#2 £.3
** = !+* + - + -+...
a3 , z6 x .
*- - + ---+.-
0^ X* X6
cos*- 1-55 + ---+..-
cos (a; sin 0) = /0(a:) + 2 {/2(» cos 20 + /4(aj) cos 4^ H ----
where Jn(x) is Bessel's function of order n,
sin (x sin 0) = 2 {«/i(z) sin 0 + ^(a;) sin 30 H ----
cos (x cos 0) = «70(a;) - 2/2(35) cos 29 + 2/4(0:) cos 4:6 -\ ----
sin (x cos 0) = 2/i(z) cos 0 — 2/3(2) cos 30 + 2/6(aO cos 50 H ----
sin (A + x sin 0) = JQ(x) sin A + /i (re) [sin (-4. + 0) - sin (A - 0)]
+ /a(aO[sin (A + 20) + sin (A - 20)]
4- /s(a:)[sin (A + 30) - sin (A - 30)]
+ /4(aO[sin (A + 40) + sin (A - 40)] H ----
10. MENSURATION
The term mensuration is used in this article to include the relations between the areas
and volumes of geometric figures and their linear dimensions.
Triangle.
Area = 1/2 (Base) X (Perpendicular height)
= Vs(s — a)(s — ty(s — c)
where a, 6, and c are the lengths of the three sides respectively, and s — 1/2 (a + 6 + c).
Trapezoid.
Area - ( ^-^ ) d
where a and 6 are the lengths of the parallel sides respectively, and d their distance apart.
Parallelogram.
Area = (Base) X (Perpendicular height)
Parabola.
Area = 2/3 (Area of circumscribing rectangle)
Cycloid.
Area = 3 UTTX (Altitude)2
the altitude being the diameter of the rolling circle.
1-18 MATHEMATICS, UNITS, AND SYMBOLS
Circle.
Circumference = 2?rr = ird
1
where r is the radius and d the diameter.
Area = xr2 = — <
4
Area of segment = — (6 — sin 0)
A
where 6 is the angle in radians (see Angles) subtended by the arc of the segment. If n is
the height of the segment, measured along the radius perpendicular to the chord,
where
Ellipse.
Area of segment = irfi M — A(r — ri)
Area = irab
where a and 6 are the principal semi-axes.
Prism with Parallel Sides and Parallel Ends.
Volume = (Area of end) X (Perpendicular distance between ends)
Right Circular Cylinder.
Volume = ~ d2 1
4
where d is the diameter and I the length.
Total surface of right cylinder = ird(l + l/%d)
Right Circular Cone.
Volume = 1/3 (Area of base) X (Height)
= !/3 (Volume of circumscribing cylinder)
where r is the radius of base and h the height of the cone.
Area of curved surface of a right circular cone = irr Vhz + r2
Right Pyramid.
Volume = 1/3 (Area of base) X (Height).
Volume of frustum of pyramid = 1/3 (Height) (A + VaA )
where A and a are the areas of the ends respectively.
Sphere.
T — radius
Area of surface = 4irr* — 2/3 (total area of circumscribing cylinder)
Area of the surface of a zone of a sphere « area of zone of the same height as this zone
projected on to a cylinder.
Volume = 4/3 xT-3 = 2/3 (volume of circumscribing cylinder)
Volume of a frustum of a sphere = ^(k ±h) — - (kz ± A3), where k is the distance
3
of its outer face from center and Ji the distance of its inner face from the center, the nega-
tive signs in the brackets to be used if both faces are on the same side of the center and
the positive signs if on opposite sides of the center.
Ellipsoid.
Volume =
where a, &, and c are the three principal semi-axes, respectively.
Paraboloid. Volume of a paraboloid of revolution equals one-half that of the circum-
scribing cylinder*
COMMON AND NATURAL LOGARITHMS OF NUMBERS 1-19
MATHEMATICAL TABLES AND CHARTS
11. COMMON AND NATURAL LOGARITHMS OF NUMBERS
The common, logarithm of a number is the index of the power to which the base 10
must be raised in order to equal the number.
The common logarithm of every positive number not an integral power of 10 consists
of an integral and a decimal part. The integral part or whole number is called the charac-
teristic and may be either positive or negative. The decimal or fractional part is a positive
number called the mantissa and is the same for all numbers which have the same sequential
digits.
The characteristic of the logarithm of any positive number greater than one is positive
and is one less than the number of digits before the decimal point.
The characteristic of the logarithm of any positive number less than one is negative
and is one more than the number of ciphers immediately after the decimal point.
A negative number or number less than zero has no real logarithm.
EXAMPLES: Logio 25400. = 4,404834 Logio 0.0254 = 2.404834 or 8.404834 — 10
The two systems of logarithms in general use are the common or Briggsian logarithms,
introduced in 1615 by Henry Briggs, a contemporary of John Napier, the inventor of
logarithms, and the natural or less appropriately termed Napierian or hyperbolic loga-
rithms, which developed somewhat accidentally from Napier's original work. The latter
have a base denoted by e, an irrational number, which is:
2.7182818
To obtain the natural logarithm, the common logarithm given below is multiplied
by loge 10 which is 2.302585, or log, N = 2.302585 logio N.
N
0
1
2
3
4
5
6
7
8
9
0
000000
301030
477121
602060
698970
778151
845098
903090
954243
1
2
3
000000
301030
477121
041393
322219
491362
079181
342423
505150
113943
361728
518514
146128
380211
531479
176091
397940
544068
204120
414973
556303
230449
431364
568202
255273
447158
579784
278754
462398
591065
4
5
6
602060
698970
778151
612784
707570
785330
623249
716003
792392
633468
724276
799341
643453
732394
806180
653213
740363
812913
662758
748188
819544
672098
755875
826075
681241
763428
832509
690196
770852
838849
7
8
9
845098
903090
954243
851258
908485
959041
857332
913814
963788
863323
919078
968483
869232
924279
973128
875061
929419
977724
880814
934498
982271
886491
939519
9867.72
892095
944483
991226
897627
949390
995635
10
000000
004321
008600
012837
017033
021189
025306
029384
033424
037426
1
2
3
041393
079181
113943
045323
082785
117271
049218
086360
120574
053078
089905
123852
056905
093422
127105
060698
096910
130334
064458
100371
133539
068186
103804
136721
071882
107210
139879
075547
110590
143015
4
5
6
146128
176091
204120
149219
178977
206826
152288
181844
209515
155336
184691
212188
158362
187521
214844
161368
190332
217484
164353
J 93 125
220108
167317
195900
222716
170262
198657
225309
173186
201397
227887
7
8
9
230449
255273
278754
232996
257679
281033
235528
260071
283301
238046
262451
285557
240549
264818
287802
243038
267172
290035
245513
269513
292256
247973
271842
294466
250420
274158
296665
252853
276462
298853
20
301030
303196
305351
307496
309630
311754
313867
315970
318063
320146
1
2
3
322219
342423
361728
324282
344392
363612
326336
346353
365488
328380
348305
367356
330414
350248
369216
332438
352183
371068
334454
354108
372912
336460
356026
374748
338456
357935
376577
340444
359835
378398
4
5
6
380211
397940
414973
382017
399674
416641
383815
401401
418301
385606
403121
419956
387390
404834
421604
389166
406540
423246
390935
408240
424882
392697
409933
426511
394452
41 1620
428135
396199
413300
429752
7
8
9
431364
447158
462398
432969
448706
463893
434569
450249
465383
436163
451786
46686S
437751
453318
468347
439333
454845
469822
440909
456366
471292
442480
457882
472756
444045
459392
474216
445604
460898
475671
30
477121
478566
480007
481443
482874
484300
485721
487133
438551
489958
1
2
3
491362
505150
518514
492760
506505
519828
494155
507856
521138
495544
509203
522444
496930
510545
523746
498311
511883
525045
499687
513218
526339
501059
514548
527630
502427
515874
528917
503791
517196
530200
4
5
531479
544068
532754
545307
534026
546543
535294
547775
536558
549003
537819
550228
539076
551450
540329
552668
541579
553883
542825
555094
1-20
MATHEMATICS, UNITS, AND SYMBOLS
N
0
1
2
3
4
5
6
7
8
9
P--
j
544068
545307
546543
547775
549003
550228
551450
552668
553883
555094
6
556303
557507
558709
559907
561101
562293
563481
564666
565848
567026
7
568202
569374
570543
571709
572872
574031
575188
576341
577492
578639
8
579784
580925
582063
583199
584331
585461
586587
587711
588832
589950
c
591065
592177
593286
594393
595496
596597
597695
598791
599883
600973
40
602060
603144
604226
605305
606381
607455
608526
609594
610660
611723
1
612784
613842
614897
615950
617000
618048
619093
620136
621176
622214
623249
624232
625312
626340
627366
628389
629410
630428
631444
632457
a
633468
634477
635484
636488
637490
638489
639486
640481
641474
642465
^
643453
644439
645422
646404
647383
648360
649335
650308
651278
652246
e
653213
654177
655138
656098
657056
658011
658965
659916
660865
661713
6
662758
663701
664642
665581
666518
667453
668386
669317
670246
671173
7
672098
673021
673942
674861
675778
676694
677607
678518
679428
680336
8
681241
682145
683047
683947
684845
685742
686636
687529
688420
689309
9
690196
691081
691965
692847
693727
694605
695482
696356
697229
698100
50
698970
699838
700704
701568
702431
703291
704151
705008
705864
706718
1
707570
708421
709270
710117
710963
711807
712650
713491
714330
715167
2
716003
716838
717671
718502
719331
720159
720986
721811
722634
723456
724276
725095
725912
726727
727541
728354
729165
729974
730782
731589
4
732394
733197
733999
734800
735599
736397
737193
737987
738781
739572
5
740363
741152
741939
742725
743510
744293
745075
745855
74663'
747412
6
748188
748963
749736
750508
751279
752048
752816
753583
754348
755112
7
755875
756636
757396
758155
758912
759668
760422
761176
761928
762679
8
763428
764176
764923
765669
766413
767156
767898
768638
769377
770115
9
770852
771587
772322
773055
773786
774517
775246
775974
776701
777427
€0
778161
778874
779596
780317
781037
781755
782473
783189
783904
784617
1
785330
786041
786751
787460
788168
788875
789581
790285
790988
791691
2
792392
793092
793790
794488
795185
795880
796574
797268
797960
798651
3
799341
800029
800717
801404
802089
802774
803457
804139
804821
805501
4
806180
806858
807535
80821 1
808886
809560
810233
810904
811575
812245
5
812913
813581
814248
814913
815578
816241
816904
817565
818226
818885
6
819544
820201
820858
821514
822168
822822
823474
824126
824776
825426
7
826075
826723
827369
828015
828660
829304
829947
830589
831230
831870
8
832509
833147
833784
834421
835056
835691
836324
836957
837588
838219
9
838849
839478
840106
840733
841359
841985
842609
843233
843855
844477
70
845098
845718
846337
846955
847573
848189
848805
849419
850033
850646
I
851258
851870
852480
853090
853698
854306
854913
855519
856124
856729
2
857332
857935
858537
859138
859739
860338
860937
861534
862131
862728
3
863323
863917
864511
865104
865696
866287
866878
867467
868056
868644
4
869232
869818
870404
870989
871573
872156
872739
873321
873902
874482
5
875061
875640
876218
876795
877371
877947
878522
879096
879669
880242
6
880814
881385
881955
882525
883093
883661
884229
884795
885361
885926
7
886491
887054
887617
888179
888741
889302
889862
890421
890980
891537
8
9
892095
897627
892651
898176
893207
898725
893762
899273
894316
899821
894870
900367
895423
900913
895975
901458
896526
902003
897077
902547
30
903090
903633
904174
904716
905256
905796
906335
908874
907411
907949
1
2
3
908485
913814
919078
909021
914343
919601
909556
914872
920123
910091
915400
920645
910624
915927
921166
911158
916454
921686
911690
916980
922206
912222
917506
922725
912753
918030
923244
913284
918555
923762
•4
•6
924279
929419
934498
924796
929930
935003
925312
930440
935507
925828
930949
936011
926342
931458
936514
926857
931966
937016
927370
932474
937518
927883
932981
938019
928396
933487
938520
928908
933993
939020
8
9
939519
944483
949390
940018
944976
949878
940516
945469
950365
941014
945961
950851
941511
946452
951338
942008
946943
951823
942504
947434
952308
943000
947924
952792
943495
948413
953276
943989
948902
953760
to
954243
954725
955207
955688
956168
956649
957128
957607
958086
958564
1
3
959041
963788
968483
959518
964260
968950
959995
964731
969416
960471
965202
969882
960946
965672
970347
961421
966142
970812
961895
966611
971276
962369
967080
971740
962843
967548
972203
963316
968016
972666
4
6
973128
977724
982271
973590
978181
982723
974051
978637
983175
974512
979093
983626
974972
979548
984077
975432
980003
984527
975891
980458
984977
976350
980912
985426
976808
981366
985875
977266
981819
986324
7 ,
8
9
986772
991 226
995635
987219
991669
996074
987666
992UI
996512
988113
992554
996949
988559
992995
997386
989005
993436
997823
989450
993877
998259
989895
994317
998695
990339
994757
999131
990783
995196
999565
100
000000
000434
000368
001301
001734
002166
002598
003029
003461
003891
TRIGONOMETRIC TABLES
1-21
12. TRIGONOMETRIC TABLES
The following tables give the values of sin x, cos x, and tan x for values of x from 0 to
90° in intervals of 0.1 degree. By making use of the periodic character of these functions,
the values can be determined from these tables for all values of x to an accuracy of 0.1
degree. (See Trigonometric Formulas.)
1 5^n
If the angle is given in radians multiply the number of radians by (57.295) to
7T
obtain the number of degrees.
Trigonometric Functions
0.0°-15.9°
Angle
in
Degrees
Name
of
Function
Value of Function for Each Tenth of a Degree
0.0
0.1
0.2
0.3
0.4
0.5
0.6
0.7
0.8
0.9
sin
0.0000
0.0017
0.0035
0.0052
0.0070
0.0087
0.0105
0.0122
0.0140
0.0157
0
C03
1.0000
1.0000
1.0000
1.0000
1.0000
1.0000
0.9999
0.9999
0.9999
0.9999
tan
0.0000
0.0017
0.0035
0.0052
0.0070
0.0087
0.0105
0.0122
0.0140
0.0157
sin
0.0175
0.0192
0.0209
0.0227
0.0244
0.0262
~0.0279
0.0297
0.0314
0.0332
1
cos
0.9998
0.9998
0.9998
0.9997
0.9997
0.9997
0.9996
0.9996
0.9995
0.9995
tan
0.0175
0.0192
0.0209
0.0227
0.0244
0.0262
0.0279
0.0297
0.0314
0.0332
sin
0.0349
0.0366
0.0384
0.0401
0.0419
0.0436
0.0454
0.0471
0.0488
0.0506
2
cos
0.9994
0.9993
0.9993
0.9992
0.9991
0.9990
0.9990
0.9989
0.9988
0.9987
tan
0.0349
0.0367
0.0384
0.0402
0.0419
0.0437
0.0454
0.0472
0.0489
0.0507
sin
0.0523
0.0541
0.0558
0.0576
0.0593
0.0610
0.0628
0.0645
0.0663
0.0680
3
cos
0.9986
0.9985
0.9984
0.9983
0.9982
0.9981
0.9980
0.9979
0.9978
0.9977
tan
0.0524
0.0542
0.0559
0.0577
0.0594
0.0612
0.0629
0.0647
0.0664
0.0682
sin
0.0698
0.0715
0.0732
0.0750
0.0767
0.0785
0.0802
0.0819
0.0837
0.0854
4
cos
0.9976
0.9974
0.9973
0.9972
0.9971
0.9969
0.9968
0.9966
0.9965
0.9963
tan
0.0699
0.0717
0.0734
0.0752
0.0769
0.0787
0.0805
0.0822
0.0840
0.0857
sin
0.0872
0.0889
0.0906
0.0924
0.0941
0.0958
0.0976
0.0993
0.1011
0.1028
5
cos
0.9962
0.9960
0.9959
0.9957
0.9956
0.9954
0.9952
0.9951
0.9949
0.9947
tan
0.0875
0.0892
0.0910
0.0928
0.0945
0.0963
0.0981
0.0998
0.1016
0.1033
sin
0.1045
0.1063
0.1080
0.1097
0.1115
0.1132
0.1149
0.1167
0.1184
0.1201
6
cos
0.9945
0.9943
0.9942
0.9940
0.9938
0.9936
0.9934
0.9932
0.9930
0.9928
tan
O.I05I
0.1069
0.1086
0.1104
0.1122
0.1139
0.1157
0.1175
0.1192
0.1210
sin
0.1219
0.1236
0.1253
0.1271
0.1288
0.1305
0.1323
0.1340
0.1357
0. 1374
7
cos
0.9925
0.9923
0.9921
0.9919
0.9917
0.9914
0.9912
0.9910
0.9907
0.9905
tan
0.1228
0.1246
0.1263
0.1281
9.1299
0.1317
0.1334
0.1352
0.1370
0.1388
sin
0.1392
0.1409
0.1426
0.1444
0.1461
0.1478
0.1495
0.1513
0.1530
0.1547
8
cos
0.9903
0.9900
0.9898
0.9895
0.9893
0.9890
0.9888
0.9885
0.9882
0.9880
tan
0.1405
0.1423
0.1441
0.1459
0.1477
0.1495
0.1512
0.1530
0.1548
0.1566
sin
0.1564
0.1582
0.1599
0.1616
0.1633
0.1650
0.1663
0.1685
0.1702
0.1719
9
cos
0.9877
0.9874
0.9871
0.9869
0.9866
0.9863
0.9860
0.9857
0.9854
0.9851
tan
0,1584
0.1602
0.1620
0.1638
0.1655
0.1673
0.1691
0.1709
0.1727
0.1745
sin
0.1736
0.1754
O.I77I
0.1788
0.1805
0.1822
0.1840
0.1857
0.1874
0.1891
10
cos
0.9848
0.9845
0.9842
0.9839
0.9836
0.9833
0.9829
0.9826
0.9823
0.9820
tan
0.1763
0.1781
0.1799
0.1817
0.1835
0.1853
0.1871
0.1890
0.1908
0.1926
sin
0.1908
0.1925
0.1942
0.1959
0.1977
0.1994
0.2011
0.2028
0.2045
0.2062
11
cos
0.9816
0.9813
0.9810
0.9806
0.9803
0.9799
0.9796
0.9792
0.9789
0.9785
tan
0.1944
0.1962
0.1980
0.1998
0.2016
0.2035
0.2053
0.2071
0.2089
0.2107
sin
0.2079
02096
0.2113
0.2130
0.2147
0.2164
0.2181
0.2198
0.2215
0.2232
12
cos
0.9781
0.9778
0.9774
0.9770
0.9767
0.9763
0.9759
0.9755
0.9751
0.9748
tan
0.2126
0.2144
0.2162
0.2180
0.2199
0.2217
0.2235
0.2254
0.2272
0.2290
sin
0.2250
0.2267
0.2284
0.2300
0.2317
0.2334
0.2351
0.2368
0.2385
0.2402
13
cos
0.9744
0.9740
0.9736
9.9732
0.9728
0.9724
0.9720
0.9715
0.9711
0.9707
tan
0.2309
0.2327
0.2345
0.2364
0.2382
0.2401
0.2419
0.2438
0.2456
0.2475
sin
0.2419
0.2436
0.2453
0.2470
0.2487
0.2504
0.2521
0.2538
0.2554
0.2571
14
cos
0.9703
0.9699
0.9694
0.9690
0.9686
0.9681
0.9677
0.9673
0.9668
0.9664
tan
0.2493
0.2512
0.2530
0.2549
0.2568
0.2586
0.2605
0.2623
0.2642
0.2661
sin
0.2588
0.2605
0.2622
0.2639
0.2656
0.2672
0.2689
0.2706
0.2723
0.2740
15
cos
0.9659
0.9655
0.9650
0.9646
0.9641
0.9636
0.9632
0.9627
0.9622
0.9617
tan
0.2679
0.2698
0.2717
0.2736
0.2754
0.2773
0.2792
0.2811
0.2830
0.2849
1-22
MATHEMATICS, UNITS, AND SYMBOLS
Trigonometric Functions
16.0°-35.9°
Angle
in
Degrees
Name
of
Function
Value of Function for Each Tenth of a Degree
0.0
0.1
0.2
0.3
0.4
0.5
0.6
0.7
0.8
0.9
—
sin
0.2756
0.2773
0.2790
0.2807
0.2823
0 2840
0.2857
0.2874
0.2890
0.2907
16
cos
0.9613
0.9608
0.9603
0.9598
0.9593
0.9588
0.9583
0.9578
0.9573
0.9568
tan
0.2867
0.2886
0.2905
0.2924
0.2943
0.2962
0.2981
0.3000
0.3019
0.3038
sin
0.2924
0.2940
0.2957
0.2974
0.2990
0.3007
0.3024
0.3040
0.3057
0.3074
17
cos
0.9563
0.9558
0.9553
0.9548
0 9542
0.9537
0.9532
0.9527
0.9521
0.9516
tan
0.3057
0.3076
0.3096
0.3115
0.3134
0.3153
0.3172
0.3191
0.3211
0.3230
sin
0.3090
0.3107
0.3123
0.3140
0.3156
0.3173
0.3190
0.3206
0.3223
0.3239
18
cos
0.95II
0.9505
0.9500
0.9494
0.9489
0.9483
0.9478
0.9472
0.9466
0.9461
tan
0.3249
0.3269
0.3288
0.3307
0.3327
0.3346
0.3365
0.3385
0.3404
0.3424
sin
0.3256
0.3272
0.3289
0.3305
0.3322
0.3338
0.3355
0.3371
0.3387
0.3404
19
cos
0 9455
0.9449
0.9444
0.9438
0.9432
0.9426
0.9421
0.9415
0.9409
0.9403
tan
0.3443
0.3463
0.3482
0.3502
0.3522
0.3541
0.3561
0.3581
0.3600
0.3620
sin
0.3420
0.3437
0.3453
0.3469
0.3486
0.3502
0.3518
0.3535
0.3551
0.3567
20
cos
0.9397
0.9391
0.9385
0.9379
0.9373
0.9367
0.9361
0.9354
0.9348
0.9342
tan
0.3640
0.3659
0.3679
0.3699
0.3719
0.3739
0.3759
0.3779
0.3799
0.3819
sin
0.3584
0.3600
0.3616
0.3633
0.3649
0.3665
0.3681
0.3697
0.3714
0.3730
21
cos
0.9336
0.9330
0.9323
0.9317
0.9311
0.9304
0.9298
0.9291
0.9285
0.9278
tan
0.3839
0.3859
0.3879
0.3899
0.3919
0.3939
0.3959
0.3979
0.4000
0.4020
sin
0.3746
0.3762
0.3778
0.3795
0.3811
0.3827
0.3843
0.3859
0.3875
0.3891
22
cos
0.9272
0.9265
0.9259
0.9252
0.9245
0.9239
0.9232
0.9225
0.9219
0.9212
tan
0.4040
0.4061
0.4081
0.4101
0.4122
0.4142
0.4163
0.4183
0.4204
0.4224
sin
0.3907
0.3923
0.3939
0.3955
0.3971
0.3987
0.4003
0.4019
0.4035
0.4051
23
cos
0.9205
0.9198
0.9191
0.9184
0.9178
0.9171
0.9164
0.9157
0.9150
0.9143
tan
0.4245
0.4265
0.4286
0.4307
0.4327
0.4348
0.4369
0.4390
0.4411
0.4431
sin
0.4067
0.4083
0.4099
0.4115
0.4131
0.4147
0.4163
0.4179
0.4195
0.4210
24
cos
0.9135
0.9128
0.9121
0.9114
0.9107
0.9100
0.9092
0.9085
0.9078
0.9070
tan
0.4452
0.4473
0.4494
0.4515
0.4536
0.4557
0.4578
0.4599
0.4621
0.4642
sin
0.4226
0.4242
0.4258
0.4274
0.4289
0.4305
0.4321
0.4337
0.4352
0.4368
25
cos
0.9063
0.9056
0.9048
0.9041
0.9033
0.9026
0.9018
0.9011
0.9003
0.8996
tan
0.4663
0.4684
0.4706
0.4727
0.4748
0.4770
0.4791
0.4813
0.4834
0.4856
sin
0.4384
0.4399
0.4415
0.4431
0.4446
0.4462
0.4478
0.4493
0.4509
0.4524
26
cos
0.8988
0.8980
0.8973
0.8965
0.8957
0.8949
0.8942
0.8934
0.8926
0.8918
tan
0.4877
0.4899
0.4921
0.4942
0.4964
0.4986
0.5008
0.5029
0.5051
0.5073
sin
0.4540
0.4555
0.4571
0.4586
0.4602
0.4617
0.4633
0.4648
0.4664
0.4679
27
cos
0.8910
0.8902
0.8894
0.8886
0.8878
0.8870
0.8862
0.8854
0.8846
0.8838
tan
0.5095
0.5117
0.5139
0.5161
0.5184
0.5206
0.5228
0.5250
0.5272
0.5295
sin
0.4695
0.4710
0.4726
0.4741
0.4756
0.4772
0.4787
0.4802
0.4818
0.4833
28
cos
0.8829
0.8821
0.8813
0.8805
0.8796
0.8788
0.8780
0.8771
0.8763
0.8755
tan
0.53J7
0.5340
0.5362
0.5384
0.5407
0.5430
0.5452
0.5475
0.5498
0.5520
sin
0.4848
0.4863
0.4879
0.4894
0.4909
0.4924
0.4939
0.4955
0.4970
0.4985
29
cos
0.8746
0.8738
0.8729
0.8721
0.8712
0.8704
0.8695
0.8686
0.8678
0.8669
tan
0.5543
0,5566
0.5589
0.5612
0.5635
0.5658
0.5681
0.5704
0.5727
0.5750
sin
0.5000
0.5015
0.5030
0.5045
0.5060
0.5075
0.5090
0.5105
0.5120
0.5135
30
cos
0.8660
0.8652
0.8643
0.8634
0.8625
0.8616
0 8607
0.8599
0.8590
0.8581
tan
0.5774
0.5797
0.5820
0.5844
0.5867
0.5890
0.5914
0.5938
0.5961
0.5985
sin
0.5150
0.5165
0.5180
0.5195
0.5210
0.5225
0.5240
0.5255
0.5270
0.5284
31
cos
0.8572
0.8563
0.8554
0.8545
0.8536
0.8526
0.8517
0.8508
0.8499
0.8490
fofl
0.6009
0.6032
0.6056
0.6080
0,6104
0.6128
0.6152
0.6176
0.6200
0.6224
sin
0.5299
0.5314
0.5329
0.5344
0.5358
0.5373
0.5388
0.5402
0.5417
0.5432
32
cos
0.8480
0.8471
0.8462
0.8453
0.8443
0.8434
0.8425
0.8415
0.8406
0.8396
tan
0.6249
0.6273
0.6297
0.6322
0.6346
0.6371
0.6395
0.6420
0.6445
0.6469
sin
0.5446
0.5461
0.5476
0.5490
0.5505
0.5519
0.5534
0.5548
0.5563
0.5577
33
cos
0.8387
0.8377
0.8368
0.8358
0.8348
0.8339
0.8329
0.8320
0.8310
0.8300
tan
0.6494
0.6519
0.6544
0.6569
0.6594
0.6619
0.6644
0.6669
0.6694
0.6720
sin
0.5592
0.5606
0.5621
0.5635
0.5650
0.5664
0.5678
0.5693
0.5707
0.5721
34
cos
0.8290
0.8281
0.8271
0.8261
0.8251
0.8241
0.8231
0.8221
0.8211
0.8202
tan
0.6745
0.6771
0.6796
0.6822
0.6847
0.6873
0.6899
0.6924
0.6950
0.6976
sin
0.5736
0.5750
0.5764
0.5779
0.5793
0.5807
0.5821
0.5835
0.5850
0.5864
35
cos
0.8192
0.8181
0.8I7I
0.8161
0.8151
0.8141
0,8131
0,8121
0.8111
0.8100
tan
0.7002
0.7028
0.7054
0.7080
0.7107
0,7133
0,7159
0,7186
0.7212
0.7239
TRIGONOMETRIC TABLES
1-23
Trigonometric Functions
36.0°-55.9°
Angle
in
Degrees
Name
of
Function
Value of Function for Each Tenth of a Degree
0.0
0.1
0.2
0.3
0.4
0.5
0.6
0.7
0.8
0.9
sin
0.5878
0.5892
0.5906
0.5920
0.5934
0.5948
0.5962
0.5976
0.5990
0.6004
36
cos
0.8090
0.8080
0.8070
0.8059
0.8049
0.8039
0.8028
0.8018
0.8007
0.7997
tan
0.7265
0.7292
0.7319
0.7346
0.7373
0.7400
0.7427
0.7454
0.7481
0.7508
sin
0.6018
0.6032
0.6046
0.6060
0.6074
0.6088
0.6101
0.6115
0.6129
0.6143
37
cos
0.7986
0.7976
0 7965
0.7955
0.7944
0.7934
0.7923
0.7912
0.7902
0.7891
tan
0.7536
0.7563
0.7590
0.7618
0.7646
0.7673
0.7701
0.7729
0.7757
0.7785
sin
0.6157
0.6170
0.6184
0.6198
0.6211
0.6225
0.6239
0.6252
0.6266
0.6280
38
cos
0.7880
0.7869
0.7859
0.7848
0.7837
0.7826
0.7815
0.7804
0.7793
0.7782
tan
0.7813
0.7841
0.7869
0.7898
0.7926
0.7954
0.7983
0.8012
0.8040
0.8069
sin
0.6293
0.6307
0.6320
0.6334
0.6347
0.6361
0.6374
0.6388
0.6401
0.6414
39
cos
0.7771
0.7760
0.7749
0.7738
0.7727
0.7716
0.7705
0.7694
0.7683
0.7672
tan
0.8098
0.8127
0.8156
0.8185
0.8214
0.8243
0.8273
0.8302
0.8332
0.8361
sin
0.6428
0.6441
0,6455
0.6468
0.6481
0.6494
0.6508
0.6521
0.6534
0.6547
40
cos
0.7660
0.7649
0.7638
0.7627
0.7615
0.7604
0.7593
0.7581
0.7570
0.7559
tan
0.8391
0.8421
0.8451
0.8481
0.8511
0.8541
0.8571
0.8601
0.8632
0.8662
sin
0.6561
0.6574
0.6587
0.6600
0.6613
0.6626
0.6639
0.6653
0.6665
0.6678
41
cos
0.7547
0.7536
0.7524
0.7513
0.7501
0.7490
0.7478
0.7466
0.7455
0.7443
tan
0.8693
0.8724
0.8754
0.8785
0.8816
0.8847
0.8878
0.8910
0.8941
0.8972
sin
0.6691
0.6704
0.6717
0.6730
0.6743
0.6756
0.6769
0.6782
0.6794
0.6807
42
cos
0.7431
0.7420
0.7408
0.7396
0.7385
0.7373
0.7361
0.7349
0.7337
0.7325
tan
0.9004
0.9036
0.9067
0.9099
0.9131
0.9163
0.9195
0.9228
0.9260
0.9293
sin
0.6820
0.6833
0.6845
0.6858
0.6871
0.6884
0.6896
0.6909
0.6921
0.6934
43
cos
0.7314
0.7302
0.7290
0.7278
0.7266
0.7254
0.7242
0.7230
0.7218
0.7206
tan
0.9325
0.9358
0.9391
0.9424
0.9457
0.9490
0.9523
0.9556
0.9590
0.9623
sin
0.6947
0.6959
0.6972
0.6984
0.6997
0.7009
0.7022
0.7034
0.7046
0.7059
44
cos
0.7193
0.7181
0.7169
0.7157
0.7145
0.7133
0.7120
0.7108
0.7096
0.7083
tan
0.9657
0.9691
0.9725
0.9759
0.9793
0.9827
0.9861
0.9896
0.9930
0.9965
sin
0.7071
0.7083
0.7096
0.7108
0.7120
0.7133
0.7145
0.7157
0.7169
0.7181
45
coa
0.7071
0.7059
0.7046
0.7034
0.7022
0.7009
0.6997
0.6984
0.6972
0.6959
tan
I. 0000
1.0035
1.0070
1.0105
1.0141
1.0176
1.0212
1.0247
1.0283
1.0319
sin
0.7193
0.7206
0.7218
0.7230
0.7242
0.7254
0.7266
0.7278
0.7290
0.7302
46
cos
0.6947
0.6934
0.6921
0.6909
0.6896
0.6884
0.6871
0.6858
0.6845
0.6833
tan
1.0355
1.0392
1.0428
1.0464
1.0501
1.0538
1.0575
1.0612
1.0649
1.0686
sin
0.7314
0.7325
0.7337
0.7349
0.7361
0.7373
0.7385
0.7396
0.7408
0.7420
47
cos
0.6820
0.6807
0.6794
0.6782
0.6769
0.6756
0.6743
0.6730
0.6717
0.6704
tan
1.0724
1.0761
1.0799
1.0837
1.0875
1.0913
1.0951
I .0990
1.1028
1.1067
sin
0.7431
0.7443
0.7455
0.7466
0.7478
0.7490
0.7501
0.7513
0.7524
0.7536
48
cos
0.6691
0.6678
0.6665
0.6652
0.6639
0.6626
0.6613
0.6600
0.6587
0.6574
tan
1.1106
1.1145
1.1184
1.1224
1.1263
1.1303
1.1343
1.1383
1.1423
1.1463
sin
0.7547
0.7559
0.7570
0.7581
0.7593
0.7604
0.7615
0.7627
0.7638
0.7649
49
cos
0.6561
0.6547
0.6534
0.6521
0.6508
0.6494
0.6481
0.6468
0.6455
0.6441
tan
1 . 1504
1.1544
1.1585
1.1626
1.1667
1.1708
1.1750
1.1792
1.1833
1.1875
sin
0.7660
0.7672
0.7683
0.7694
0.7705
0.7716
0.7727
0.7738
0.7749
0.7760
50
cos
0.6428
0.6414
0.6401
0.6388
0.6374
0.6361
0.6347
0.6334
0.6320
0.6307
tan
1.1918
1.1960
1.2002
1 .2045
1 .2088
1.2131
1.2174
1.2218
1.2261
1.2305
sin
0.7771
0.7782
0.7793
0.7804
0.7815
0.7826
0.7837
0.7848
0.7859
0.7869
51
cos
0.6293
0.6280
0.6266
0.6252
0.6239
0.6225
0.6211
0.6198
0.6184
0.6170
tan
1.2349
1 .2393
1 .2437
1 .2482
1.2527
1.2572
1.2617
1.2662
I. 2708
1.2753
sin
0.7880
0.789.1
0.7902
0.7912
0.7923
0.7934
0.7944
0.7955
0.7965
0.7976
52
cos
0.6157
0.6143
0.6129
0.6115
0.6101
0.6088
0.6074
0.6060
0.6046
0.6032
tan
1.2799
1 .2846
1 .2892
1.2938
1.2985
1 .3032
1.3079
1.3127
1.3175
1.3222
sin
0.7986
0.7997
0.8007
0.8018
0.8028
0.8039
0.8049
0.8059
0.807d
0.8080
53
cos
0.6018
0.6004
0.5990
0.5976
0.5962
0.5948
0.5934
0.5920
0.5906
0.5892
tan
1.3270
1.3319
1.3367
1.3416
1.3465
1.3514
1.3564
1.3613
1.3663
1.3713
sin
0.8090
0.8100
0.8111
0.8121
0.8131
0.8141
0.8151
0.8161
0.8171
0.8181
54
cos
0.5878
0.5864
0.5850
0.5835
0.5821
0.5807
0.5793
0.5779
0.5764
0.5750
tan
1.3764
1.3814
1.3865
1.3916
1.3968
1.4019
1.4071
1.4124
1.4176
1.4229
sin
0.8192
0.8202
0.8211
0.8221
0.8231
0.8241
0.8251
0.8261
0.8271
0.8281
55
cos
0.5736
0.5721
0.5707
0.5693
0.5678
0.5664
0.5650
0.5635
0.5621
0.5606
tan
1.4281
1.4335
1.4388
1.4442
1.4496
1.4550
1.4605
1.4659
1.4715
1.4770
1-24
MATHEMATICS, UNITS, AND SYMBOLS
Trigonometric Functions
56.0°-75.9°
Angle
"~
Name
. . — ~
Value of Function for Each Tenth of a Degree
in
Degrees
of
Function
0.0
0.1
0.2
0.3
0.4
0.5
0.6
0.7
0.8
0.9
56
sin
cos
tan
.8290
.5592
.4826
0.8300
0.5577
1.4882
0.8310
0.5563
1 .4938
0.8320
0.5548
1.4994
0.8329
0.5534
1.5051
0.8339
0.5519
1.5108
0.8348
0.5505
1.5166
0.8358
0.5490
1.5224
0.8368
0.5476
1.5282
0.8377
0.5461
1.5340
57
sin
cos
tan
.8387
.5446
.5399
0.8396
0.5432
1.5458
0.8406
0.5417
1.5517
0.8415
0.5402
1.5577
0.8425
0.5388
1 .5637
0.8434
0.5373
1.5697
0.8443
0.5358
1.5757
0.8453
0.5344
1.5818
0.8462
0.5329
1.5880
0.8471
0.5314
I .5941
58
sin
cos
tan
0.8480
0.5299
.6003
0.8490
0.5284
1.6066
0.8499
0.5270
1.6128
0.8508
0.5255
1.6191
0.8517
0.5240
1.6255
0.8526
0.5225
1.6319
0.8536
0.5210
1.6383
0.8545
0.5195
1.6447
0.8554
0.5180
1.6512
0.856?
0.5165
1.6577
59
sin
cos
tan
0.8572
0.5150
.6643
0.8581
0.5135
1 .6709
0.8590
0.5120
1.6775
0.8599
0.5105
1.6842
0.8607
0.5090
1 .6909
0.8616
0.5075
1.6977
0.8625
0.5060
1.7045
0.8634
0.5045
1.7113
0.8643
0.5030
1.7182
0.8652
0.5015
1.7251
60
sin
cos
tan
0.8660
0.5000
.7321
0.8669
0.4985
1.7391
0.8678
0.4970
1.7461
0.8686
0.4955
1.7532
0.8695
0.4939
1.7603
0.8704
0.4924
1.7675
0.8712
0.4909
1.7747
0.8721
0.4894
1.7820
0.8729
0.4879
1.7893
0.8738
0.4863
1.7966
61
sin
cos
tan
0.8746
0.4848
1.8040
0.8755
0.4833
1.8115
0.8763
0.4818
1.8190
0.8771
0.4802
1.8265
0.8780
0.4787
1.8341
0.8788
0.4772
1.8418
0.8796
0.4756
1.8495
0.8805
0.4741
1.8572
0.8813
0.4726
1.8650
0.8821
0.4710
1.8728
62
sin
cos
tan
0.8829
0.4695
1.8807
0.8838
0.4679
1.8887
0.8846
0.4664
1.8967
0.8854
0.4648
1.9047
0.8862
0.4633
1.9128
0.8870
0.4617
1.9210
0.8878
0.4602
1 .9292
0.8886
0.4586
1 .9375
0.8894
0.4571
1.9458
0.8902
0.4555
1.9542
0.8910
0.8918
0.8926
0.8934
0.8942
0.8949
0.8957
0.8965
0.8973
0.8980
63
cos
tan
0.4540
1.9626
0.4524
1.9711
0.4509
1 .9797
0.4493
1.9883
0.4478
1.9970
0.4462
2.0057
0.4446
2.0145
0.4431
2.0233
0.4415
2.0323
0.4399
2.0413
0.8988
0.8996
0.9003
0.9011
0.9018
0.9026
0.9033
0.9041
0.9048
0.9056
64
cos
0.4384
0.4368
0.4352
0.4337
0.4321
0.4305
0.4289
0.4274
0.4258
0.4242
tan
2.0503
2.0594
2.0686
2.0778
2.0872
2.0965
2.1060
2.1155
2.1251
2.1348
.
0.9063
0.9070
0.9078
0.9085
0.9092
0.9100
0.9107
0.9114
0.9121
0.9128
65
cos
0.4226
0.4210
0.4195
0.4179
0.4163
0.4147
0.4131
0.4115
0.4099
0.4083
tan
2.1445
2.1543
2.1642
2.1742
2.1842
2.1943
2.2045
2.2148
2.2251
2.2355
.
0.9135
0.9143
0.9150
0.9157
0.9164
0.9171
0.9178
0.9184
0.9191
0.9198
66
cos
0.4067
0.4051
0.4035
0.4019
0.4003
0.3987
0.3971
0.3955
0.3939
0.3923
tan
2.2460
2.2566
2.2673
2.2781
2.2889
2.2998
2.3109
2.3220
2.3332
2.3445
sin
0.9205
0.9212
0.9219
0.9225
0.9232
0.9239
0.9245
0.9252
0.9259
0.9265
67
cos
0.3907
0.3891
0.3875
0,3859
0.3843
0.3827
0.3811
0.3795
0.3778
0.3762
tan
2.3559
2.3673
2.3789
2.3906
2.4023
2.4142
2.4262
2.4383
2.4504
2.4627
sin
0.9272
0.9278
0.9285
0.9291
0.9298
0.9304
0.9311
0.9317
0.9323
0.9330
68
cos
0.3746
0.3730
0.3714
0.3697
0.3681
0.3665
0.3649
0.3633
0.3616
0.3600
tan
2.4751
2.4876
2.5002
2.5129
2.5257
2.5386
2.5517
2.5649
2.5782
2.5916
sin
0.9336
0.9342
0.9348
0.9354
0.9361
0.9367
0.9373
0.9379
0.9385
0.9391
69
cos
0.3584
0.3567
0.3551
0.3535
0.3518
0.3502
0.3486
0.3469
0.3453
0.3437
tan
2.6051
2.6187
2.6325
2.6464
2.6605
2.6746
2.6889
2.7034
2.7179
2.7326
sin
0.9397
0.9403
0.9409
0.9415
0.9421
0.9426
0.9432
0.9438
0.9444
0.9449
70
cos
0.3420
0.3404
0,3387
0.3371
0.3355
0.3338
0.3322
0.3305
0.3289
0.3272
tan
2.7475
2.7625
2.7776
2.7929
2.8083
2.8239
2.8397
2.8556
2.8716
2.8878
sin
0.9455
0.9461
0.9466
0.9472
0.9478
0.9483
0.9489
0.9494
0.9500
0.9505
71
cos
0.3256
0.3239
0.3223
0.3206
0.3190
0.3173
0.3156
0.3140
0.3123
0.3107
tan
2.9042
2.9208
2.9375
2.9544
2.9714
2.9887
3.0061
3.0237
3.0415
3.0595
sin
0.9511
0.9516
0.9521
0.9527
0.9532
0.9537.
0.9542
0.9548
0.9553
0.9558
72
cos
0.3090
0.3074
0.3057
0.3040
0.3024
0.3007
0.2990
0.2974
0.2957
0.2940
tan
3.0777
3.0961
3.1146
3.1334
3.1524
3.1716
3.1910
3.2106
3.2305
3.2506
sin.
0.9563
0.9568
0.9573
0.9578
0.9583
0.9588
0.9593
0.9598
0.9603
0.9608
73
COB
0.2924
0.2907
0.2890
0.2874
0.2857
0.2840
0.2823
0.2807
0.2790
0.2773
tan
3.2709
3.2914
3.3122
3.3332
3.3544
3.3759
3.3977
3.4197
3.4420
3.4646
sin
0.9613
0.9617
0.9622
0.9627
0.9632
0.9636
0.9641
0.9646
0.9650
0.9655
74
cos
0.2756
0.2740
0.2723
0.2706
0.2689
0.2672
0.2656
0.2639
0.2622
0.2605
tan
3.4874
3.5105
3.5339
3.5576
3.5816
3.6059
3.6305
3.6554
3.6806
3.7062
sin
0.9659
0.9664
0.9668
0.9673
0.9677
0.9681
0.9686
0.9690
0.9694
0.9699
75
COB
0.2588
0.2571
0.2554
0.2538
0.2521
0.2504
0.2487
0.2470
0.2453
0.2436
tan
3.7321
3.7583
3.7848
3.8118
3.8391
3.8667
3.8947
3.9232
3.9520
3.9812
TRIGONOMETRIC TABLES
1-25
Trigonometric Functions
76.0°-89.9°
Angle
in
Degrees
Name
of
Function
Value of Function for Each Tenth of a Degree
0.0
0.1
0.2
0.3
0.4
0.5
0.6
0.7
0.8
0.9
76
sin
cos
tan
0.9703
0.2419
4.0108
0.9707
0.2402
4.0408
0.9711
0.2385
4.0713
0.9715
0.2368
4.1022
0.9720
0.2351
4.1335
0.9724
0.2334
4.1653
0.9728
0.2317
4.1976
0.9732
0.2300
4.2303
0.9736
0.2284
4.2635
0.9740
0.2267
4.2972
77
sin
cos
tan
0.9744
0.2250
4.3315
0.9748
0.2232
4.3662
0.9751
0.2215
4.4015
0.9755
0.2198
4.4374
0.9759
0.2181
4.4737
0.9763
0.2164
4.5107
0.9767
0.2147
4.5483
0.9770
0.2130
4.5864
0.9774
0.2113
4.6252
0.9778
0.2096
4.6646
78
sin
cos
tan
0.9781
0.2079
4.7046
0.9785
0.2062
4.7453
0.9789
0.2045
4.7867
0.9792
0.2028
4.8288
0.9796
0.2011
4.8716
0.9799
0.1994
4.9152
0.9803
0.1977
4.9594
0.9806
0.1959
5.0045
0.9810
0.1942
5.0504
0.9813
0.1925
5.0970
79
sin
cos
tan
0.9816
0.1908
5.1446
0.9820
0.1891
5.1929
0.9823
0.1874
5.2422
0.9826
0.1857
5.2924
0.9829
0.1840
5.3435
0.9833
0.1822
5.3955
0.9836
0.1805
5.4486
0.9839
0.1788
5.5026
0.9842
0.1771
5.5578
0.9845
0.1754
5.6140
80
sin
cos
tan
0.9848
0.1736
5.6713
0.9851
0.1719
5.7297
0.9854
0.1702
5.7894
0.9857
0.1685
5.8502
0.9860
0.1668
5.9124
0.9863
0.1650
5.9758
0.9866
0.1633
6.0405
0.9869
0.1616
6.1066
0.9871
0.1599
6.1742
0.9874
0.1582
6.2432
81
sin
cos
tan
0.9877
0.1564
6.3138
0.9880
0.1547
6.3859
0.9882
0.1530
6.4596
0.9885
0.1513
6.5350
0.9888
0.1495
6.6122
0.9890
0.1478
6.6912
0.9893
0.1461
6.7720
0.9895
0.1444
6.8548
0.9898
0.1426
6.9395
0.9900
0.1409
7.0264
82
sin
cos
tan
0.9903
0.1392
7.1154
0.9905
0.1374
7.2066
0.9907
0.1357
7.3002
0.9910
0.1340
7.3962
0.9912
0.1323
7.4947
0.9914
0.1305
7.5958
0.9917
0.1288
7.6996
0.9919
0.1271
7.8062
0.9921
0.1253
7.9158
0.9923
0.1236
8.0285
83
sin
cos
tan
0.9925
0.1219
8.1443
0.9928
0.1201
8.2636
0.9930
0.1184
8.3863
0.9932
0.1167
8.5126
0.9934
0.1149
8.6427
0.9936
0.1132
8.7769
0.9938
0.1115
8.9152
0.9940
0.1097
9.0579
0.9942
0.1080
9.2052
0.9943
0.1063
9.3572
84
sin
cos
tan
0.9945
0.1045
9.5144
0.9947
0.1028
9.6768
0.9949
0.1011
9.8448
0.9951
0.0993
10.02
0.9952
0.0976
10.20
0.9954
0.0958
10.39
0.9956
0.0941
10.58
0.9957
0.0924
10.78
0.9959
0.0906
10.99
0.9960
0.0889
11.20
85
sin
cos
tan
0.9962
0.0872
11.43
0.9963
0.0854
11.66
0.9965
0.0837
11.91
0.9966
0.0819
12.16
0.9968
0.0802
12.43
0.9969
0.0785
12.71
0.9971
0.0767
13.00
0.9972
0.0750
13.30
0.9973
0.0732
13.62
0.9974
0.0715
13.95
86
sin
cos
tan
0.9976
0.0698
14.30
0.9977
0.0680
14.67
0.9978
0.0663
15.06
0.9979
0.0645
15.89
0.9980
0.0628
15.46
0.9981
0.0610
16.35
0.9982
0.0593
16.83
0.9983
0.0576
17.34
0.9984
0.0558
17.89
0.9985
0.0541
18.46
87
sin
cos
tan
0.9986
0.0523
19.08
0.9987
0.0506
19.74
0.9988
0.0488
20.45
0.9989
0.0471
21.20
0.9990
0.0454
22.02
0.9990
0.0436
22.90
0.9991
0.0419
23.86
0,9992
0.0401
24.90
0.9993
0.0384
26.03
0.9993
0.0366
27.27
88
sin
cos
tan
0.9994
0.0349
28.64
0.9995
0.0332
30.14
0.9995
0.0314
31.82
0.9996
0.0297
33.69
0.9996
0.0279
35.80
0.9997
0.0262
38.19
0.9997
0.0244
40.92
0.9997
0.0227
44.07
0.9998
0.0209
47.74
0.9998
0.0192
52.08
89
sin
cos
tan
0.9998
0.0175
57.29
0.9999
0.0157
63.66
0.9999
0.0140
71.62
0.9999
,0.0122
81.85
0.9999
0.0105
95.49
1.000
0.0087
114.6
1.000
0.0070
H3.2 fe
1.000
0.0052
191.0
1.000
0.0035
286.5
1.000
0.0017
573.0
1-26
MATHEMATICS; UNITS, AND SYMBOLS
13. EXPONENTIAL AND HYPERBOLIC TABLES
The following tables give values of «*, e"*, sinh x, cosh x and tanh x for values of a:
from 0.00 to 6.00 in intervals of 0.01.
To facilitate computations involving multiplication, the common logarithms of ex,
sinh xy cosh x, and tanh x are also given.
For values of x greater than 6, e* may be computed from the relationship eT = log"1
(x logio e) = log""1 0.43429#; e~x approaches zero; sinh x and cosh x are approximately
equal and become 0.5 e*; and tanh x and coth x have values approximately equal to unity.
Where more accurate values of the exponentials and functions are required they may
be computed from the following relationships.
e = 2.71828 18285
M « logio e = 0.43429 44819
e* = log-1 M:c<
- = 0.36787 94412
e
— « loge 10
M
2.30258 50930
log"1 — MX
Values of Hyperbolic Functions 0
*-« r\> «*> 4* § p
Q.X =
IX =
2
1 *
— ^cosna; =
secha; =
2
1
tanna; =
coth a; =
1
sinh #
cosh x
tanh a:
ft
7)
1
J
jf
I
77
1
7
I
I
L
/
'(
1
/
I
y
/
I
y
/
H
/
ft
^ i
H
/
i
\\
\V
/J
t i
\
\
/
1
\
^
J
^
I
;c
s
1
x
/
/
\
^
y
ffll
\
!L.
(
^
i
L-
s
(
\
\
/
,
s
\
f*
s^
s
/
•^
•«,
=* .
Cot
i
^c
Mi
€
**
^
— •— _
===asa.
BBMHIMM
•**.
V
\
.1
.— — —
"^
/
^*i
.•-
i an
1
X
/
^
s
^
s,
~
*
^
^
•'r
0
?
*•
Se
^c
h~
A-
v
>-4
^
»**.
^
*•
-^^
=BB- — -i
«= =
) I 2
3
4
Hyperbolic Radians (x)
Chart of the Hyperbolic Functions.
EXPONENTIAL AND HYPERBOLIC TABLES
1-27
X
Natural Values
Common Logarithms
6s
e~*
Sinh.3
Cosh a;
Tanha?
G*
Sink a:
Coshx
Tanha;
0.00
1.0000
1.0000
0.0000
1.0000
.00000
0.00000
— 00
0.00000
— 00
0.01
0.02
0.03
.0101
.0202
.0305
.99005
.98020
.97045
0.0100
0.0200
0.0300
1.0001
1.0002
1.0005
.01000
.02000
.02999
.00434
.00869
.01303
2.00001
.30106
.47719
.00002
,00009
.00020
3.99999
2.30097
.47699
0.04
0.05
0.06
.0408
.0513
.0618
. 96079
.95123
.94176
0. 0400
0.0500
0.0600
1.0008
1.0013
1.0018
.03998
.04996
.05993
.01737
.02171
.02606
.60218
.69915
.77841
.00035
.00054
.00078
.60183
.69861
.77763
0.07
0.08
0.09
.0725
.0833
.0942
,93239
.92312
.91393
0.0701
0.0801
0.0901
1.0025
1.0032
1.0041
.06989
.07983
.08976
.03040
.03474
.03909
.84545
.90355
. 95483
.00106
.00139
.00176
.84439
.90216
.95307
0.10
.1052
.90484
0.1002
1.0050
.09967
0.04343
1.00072
0.00217
2.99856
0.11
0.12
0.13
.1163
.1275
.1388
.89583
.88692
.87810
0.1102
0.1203
0.1304
1.0061
1.0072
1.0085
.10956
.11943
.12927
.04777
.05212
.05646
.04227
. 08022
.11517
.00262
.00312
.00366
1.03965
.07710
.11151
0.14
0.15
0. 16
.1503
.1618
.1735
.86936
.86071
.85214
0.1405
0.1506
0.1607
1.0098
1.0113
1.0128
.13909
.14889
.15865
.06080
,06514
. 06949
. 14755
.17772
. 20597
.00424
.00487
.00554
.14330
.17285
. 20044
0.17
0.18
0, 19
.1853
.1972
.2092
.84366
.83527
.82696
0.1708
0.1810
0.1911
1.0145
1.0162
1.0181
.16838
.17808
.18775
.07383
.07817
.08252
.23254
.25762
.28136
.00625
.00700
.00779
.22629
.25062
.27357
0.20
.2214
.81873
0.2013
1.0201
.19738
0.08686
1.30392
0.00863
1.29529
0.21
0.22
0.23
.2337
.2461
.2586
.81058
.80252
.79453
0.2115
0.2218
0.2320
1.0221
1.0243
1.0266
.20697
.21652
. 22603
.09120
.09554
.09989
.32541
.34592
.36555
.00951
.01043
.01139
.31590
.33549
.35416
0.24
0.25
0.26
.2712
.2840
.2969
.78663
.77880
.77105
0.2423
0.2526
0.2629
1 . 0289
1.0314
1.0340
.23550
.24492
. 25430
.10423
.10857
.11292
.38437
.40245
.41986
.01239
.01343
.01452
.37198
.38902
.40534
0.27
0.28
0.29
.3100
.3231
.3364
.76338
.75578
.74826
0.2733
0.2837
0.2941
1.0367
1.0395
1.0423
.26362
.27291
.28213
.11726
.12160
.12595
.43663
.45282
.46847
.01564
.01681
.01801
.42099
.43601
.45046
0.30
.3499
.74082
0.3045
1.0453
.29131
0.13029
1.48362
0.01926
1.46436
0.31
0.32
0.33
.3634
.3771
.3910
.73345
.72615
.71892
0.3150
0.3255
0.3360
1.0484
1.0516
1 . 0549
.30044
.30951
.31852
.13463
.13897
.14332
.49830
.51254
.52637
.02054
.02107
.02323
.47775
.49067
.50314
0.34
0.35
0.36
.4049
.4191
.4333
.71177
.70469
,69768
0.3466
0.3572
0.3678
1.0584
1.0619
1.0655
.32748
.33638
.34521
.14766
.15200
.15635
.53981
.55290
.56564
.02463
.02607
.02755
.51513
.52682
.53809
0.37
0.38
0.39
.4477
.4623
.4770
.69073
.68386
.67706
0.3785
0.3892
0.4000
1.0692
1.0731
1.0770
.35399
.36271
.37136
.16069
.16503
.16937
.57807
.59019
.60202
.02907
.03063
.03222
.54899
.55956
.56980
0.40
1.4918
.67032
0.4108
1.0811
.37995
0.17372
1.61353
0.03385
1.67973
0.41
0.42
0.43
.5068
.5220
.5373
.66365
.65705
.65051
0.4216
0.4325
0.4434
1.0852
1.0895
1.0939
.38847
.39693
.40532
.17806
.18240
.18675
.62488
.63594
.64677
.03552
.03723
.03897
.58936
.59871
.60780
0.44
0.45
0.46
.5527
.5683
.5841
.64404
. 63763
.63128
0.4543
0.4653
0.4764
1.0984
1.1030
1.1077
.41364
.42190
.43008
.19109
.19543
.19978
.65738
.66777
.67797
.04075
.04256
.04441
.61663
.62521
.63355
0.47
0.48
0.49
.6000
.6161
.6323
.62500
.61878
.61263
0.4875
0.4986
0.5098
1.1125
1.1174
1.1225
.43820
.44624
.45422
.20412
.20846
.21280
.68797
.69779
.70744
.04630
.04822
.05018
.64167
.64957
.65726
0.50
1.6487
.60653
0.5211
1.1276
.46212
0.21715
1.71692
0.05217
1.66475
0.51
0.52
0.53
.6653
.6820
.6989
.60050
.59452
. 58860
0.5324
0.5438
0.5552
1.1329
1.1383
1.1438
.46995
.47770
.48538
.22149
.22583
.23018
.72624
.73540
.74442
.05419
.05625
,05834
.67205
.67916
.68603
0.54
0.55
0.56
.7160
.7333
.7507
.58275
.57695
.57121
0.5666
0.5782
0.5897
1.1494
1.1551
1.1609
.49299
.50052
.50798
.23452
.23886
.24320
.75330
.76204
.77065
. 06046
.06262
.06481
.69284
.69942
.70584
0.57
0.58
0.59
.7683
.7860
.8040
.56553
.55990
.55433
0.6014
0.6131
0.6248
1.1669
1.1730
1.1792
.51536
.52267
.52990
.24755
.25189
. 25623
.77914
.78751
.79576
. 06703
.06929
.07157
.71211
.71822
.72419
0.60
1.8221
.54881
0.6367
1.1855
.53705
0.26058
1.80390
0.07389
1.73001
* *
Natural Values
Common Logarithms
e*
e~*
Sinks
Cosh a;
Tanks
e*
Sinhz
Cosh re
Tanha;
0.60
1.8221
.54881
0.6367
1.1855
.53705
0.26058
1.80390
0.07389
1.73001
0.61
1.8404
.54335
0.6485
1,1919
.54413
.26492
.81194
.07624
. 73570
0 62
1.8589
.53794
0.6605
1.1984
.55113
.26926
.81987
«. 07861
.74125
0^63
1.8776
.53259
0.6725
1.2051
.55805
.27361
.82770
.08102
.74667
0.64
1.8965
.52729
0. 6846
1.2119
.56490
.27795
.83543
.08346
.75197
0 65
1 9155
.52205
0.6967
1.2188
.57167
.28229
.84308
.08593
.75715
Ol66
1.9348
.51685
0.7090
1.2258
.57836
.28663
.85063
.08843
.76220
0 67
1.9542
.51171
0.7213
1.2330
.58498
.29098
.85809
.09095
.76714
I 0*68
1.9739
.50662
0.7336
1.2402
.59152
.29532
.86548
.09351
.77197
0.69
1.9937
.50158
0.7461
1.2476
.59798
.29966
.87278
.09609
.77669
0.70
2.0138
.49659
0.7586
1.2552
.60437
0.30401
1.88000
0.09870
1.78130
0.71
2.0340
.49164
0.7712
1.2628
.61068
.30835
.88715
.10134
.78581
0 72
2.0544
.48675
0.7838
1.2706
.61691
.31269
.89423
.10401
.79022
0!73
2.0751
.48191
0.7966
1.2785
.62307
.31704
.90123
.10670
.79453
0.74
2.0959
.47711
0.8094
1.2865
.62915
.32138
.90817
.10942
.79875
0.75
2.1170
.47237
0.8223
1.2947
.63515
.32572
.91504
.11216
. 80288
0.76
2.1383
.46767
0.8353
1.3030
.64108
.33006
.92185
.11493
.80691
0.77
2. 1598
.46301
0.8484
1.3114.
.64693
.33441
.92859
,11773
.81086
0.78
2.1815
.45841
0.8615
1.3199
.65271
.33875
.93527
.12055
.81472
0,79
2.2034
.45384
0.8748
1.3286
.65841
.34309
.94190
.12340
.81850
0.80
2.2255
.44933
0.8881
1.3374
.66404
0.34744
1.94846
0.12627
1.82219
0.81
2.2479
.44486
0.9015
1.3464
.66959
.35178
.95498
.12917
.82581
0.82
2.2705
.44043
0.9150
1.3555
.67507
.35612
.96144
.13209
82935
0.83
2.2933
.43605
0.9286
1.3647
.68048
.36046
.96784
.13503
.83281
0.84
2.3164
.43171
0.9423
1.3740
.68581
.36481
.97420
.13800
83620
0.85
2.3396
.42741
0.9561
1.3835
.69107
.36915
.98051
.14099
'83952
0.86
2.3632
.42316
0.9700
1.3932
.69626
.37349
.98677
.14400
,'84277
0.87
2.3869
.41895
0.9840
1.4029
.70137
.37784
.99299
.14704
.84595
0.88
2.4109
.41478
0.9981
1.4128
.70642
.38218
.99916
.15009
' 84906
0.89
2.4351
.41066
1.0122
1.4229
.71139
.38652
0.00528
.15317
185211
0.90
2.4596
.40657
1.0265
1.4331
,71630
0.39087
0.01137
0.15627
1.85509
0.91
2.4843
.40252
.0409
1.4434
.72113
.39521
.01741
.15939
.85801
0.92
2.5093
.39852
.0554
1.4539
.72590
.39955
.02341
.16254
'86088
0.93
2.5345
.39455
.0700
1.4645
.73059
.40389
.02937
.16570
186368
0.94
0.95
0.96
2.5600
2.5857
2.6117
.39063
.38674
.38289
.0847
.0995
.1144
1.4753
1.4862
1.4973
.73522
.73978
.74428
.40824
.41258
.41692
.03530
.04119
.04704
.16888
.17208
.17531
.86642
.86910
.87173
0.97
0.98
0.99
2.6379
2.6645
2.6912
.37908
.37531
,37158
.1294
.1446
.1598
1.5085
1.5199
1.5314
.74870
.75307
.75736
.42127
.42561
.42995
.05286
.05864
.06439
.17855
.18181
.18509
.87431
.87683
.87930
1.00
2.7183
.36788
.1752
1.5431
.76159
0.43429
0.07011
0.18839
1.88172
.01
.02
.03
2.7456
2.7732
2.8011
.36422
.36059
.35701
.1907
.2063
.2220
1.5549
1.5669
1.5790
.76576
.76987
.77391
.43864
.44298
.44732
.07580
.08146
.08708
.19171
.19504
.19839
.88409
.88642
.88869
.04
, -05
,06
2.8292
2. 8577
2.8864
.35345
.34994
.34646
.2379
.2539
.2700
1.5913
1.6038
1.6164
.77789
.78181
.78566
.45167
.45601
.46035
.09268
.09825
.10379
.20176
.20515
.20855
.89092
,89310
.89524
.07
« .08
: .09
2.9154
2.9447
2.9743
.34301
.33960
.33622
.2862
.3025
.3190
1.6292
1.6421
1.6552
.78946
.79320
.79688
.46470
.46904
.47338
.10930
.11479
.12025
.21197
.21541
.21886
.89733
.89938
.90139
1 .10
3.0042
.33287
1.3356
1.6685
.80050
0.47772
0.12569
0.22233
1.90336
» .TI
! .12
.13
3.0344
3.0649
3.0957
.32956
,32628
.32303
.3524
.3693
.3863
1.6820
1.6956
1.7093
.80406
. 80757
.81102
.48207
.48641
.49075
.13111
.13649
.14186
.22582
.22931
.23283
.90529
.90718
.90903
.14
.15
.16
3.1268
3. 1582
3.1899
.31982
.31664
.31349
.4035
.4208
.4382
1.7233
1.7374
1.7517
.81441
.81775
.82104
.49510
.49944
.50378
.14720
.15253
.15783
.23636
.23990
.24346
,91085
.91262
.91436
.17
,18
.19
3.2220
3.2544
3.2871
.31037
.30728
.30*22
1.4558
1.4735
1.4914
1.7662
1.7808
1.7957
.82427
.82745
.83058
,50812
.51247
.51681
.16311
.16836
.17360
.24703
.25062
.25422
.91607
.91774
.91938
1.20
3.3201
.30119
1.5095
1.8107
.83365
0.52115
0,17882
0.25784
1.92099
EXPONENTIAL AND HYPERBOLIC TABLES
1-29
W
Natural Values
Common Logarithms
e*
e~x
Sinha;
Cosh a;
Tanha;
ex
Sinhre
Cosh a;
Tanha;
1.20
3.3201
.30119
1.5095
1.8107
.83365
0.52115
0.17882
0.25784
1.92099
.21
.22
.23
3.3535
3.3872
3.4212
.29820
.29523
.29229
.5276
.5460
.5645
.8258
.8412
.8568
.83668
.83965
.84258
.52550
.52984
.53418
.18402
.18920
.19437
.26146
.26510
.26876
.92256
.92410
.92561
.24
1 .25
.26
3.4556
3.4903
3.5254
.28938
.28650
.28365
.5831
.6019
.6209
.8725
.8884
.9045
.84546
.84828
.85106
.53853
.54287
.54721
.19951
.20464
.20975
.27242
.27610
.27979
.92709
.92854
.92996
.27
.28
.29
3.5609
3.5966
3.6328
.28083
.27804
.27527
.6400
.6593
.6788
.9208
.9373
.9540
.85380
.85648
.85913
.55155
.55590
.56024
.21485
.21993
.22499
.28349
.28721
.29093
.93135
.93272
.93406
.30
3.6693
.27253
1.6984
1.9709
.86172
0.56458
0.23004
0.29467
1.93537
.31
.32
.33
3.7062
3.7434
3.7810
. 26982
.26714
.26448
.7182
.7381
.7583
l'.9880
2.0053
2.0228
.86428
.86678
.86925
.56893
.57327
.57761
.23507
.24009
.24509
.29842
.30217
.30594
.93665
.93791
.93914
.34
.35
.36
3.8190
3.8574
3.8962
.26185
.25924
.25666
.7786
.7991
.8198
2.0404
2.0583
2.0764
.87167
.87405
.87639
.58195
.58630
.59064
.25008
.25505
.26002
.30972
.31352
.31732
.94035
.94154
.94270
.37
.38
.39
3.9354
3.9749
4.0149
.25411
.25158
.24908
.8406
.8617
.8829
2.0947
2.1132
2.1320
.87869
.88095
.88317
.59498
.59933
.60367
.26496
.26990
.27482
.32113
.32495
.32878
.94384
.94495
.94604
.40
4.0552
.24660
1.9043
2.1509
.88535
0.60801
0.27974
0.33262
1.94712
.41
.42
.43
4.0960
4.1371
4 '787
.24414
.24171
.23931
.9259
.9477
.9697
2.1700
2.1894
2.2090
.88749
.88960
.89167
.61236
.61670
.62104
.28464
.28952
.29440
.33647
.34033
.34420
.94817
.94919
.95020
.44
.45
.46
4.2207
4.2631-
4.3060
.23693
.23457
.23224
1.9919
2.0143
2.0369
2.2288
2.2488
2.2691
.89370
.89569
.89765
.62538
.62973
.63407
.29926
.30412
.30896
.34807
.35196
.35585
.95119
.95216
.95311
.47
.48
.49
4.3492
4.3929
4.4371
.22993
.22764
. 22537
2.0597
2.0827
2.1059
2.2896
2.3103
2.3312
.89958
.90147
.90332
.63841
.64276
.64710
.31379
.31862
.32343
.35976
.36367
.36759
.95404
.95495
.95584
.60
4.4817
.22313
2.1293
2.3524
.90515
0.65144
0.32823
0.37151
1.95672
.51
.52
.53
4.5267
4.5722
4.6182
.22091
.21871
.21654
2.1529
2.1768
2.2008
2.3738
2.3955
2.4174
.90694
.90870
.91042
.65578
.66013
.66447
.33303
.33781
.34258
.37545
.37939
.38334
.95758
.95842
.95924
.54
.55
.56
4.6646
4.7115
4.7588
.21438
.21225
.21014
2.2251
2.2496
2.2743
2.4395
2.4619
2.4845
.91212
.91379
.91542
.66881
.67316
.67750
.34735
.35211
.35686
.38730
.39126
.39524
.96005
.96084
.96162
.57
.58
.59
4.8066
4.8550
4.9037
.20805
.20598
. 20393
2.2993
2.3245
2.3499
2.5073
2.5305
2.5538
.91703
.91860
.92015
.68184
.68619
. 69053
.36160
.36633
.37105
.39921
.40320
.40719
.96238
.96313
.96386
1.60
4.9530
.20190
2.3756
2.5775
.92167
0.69487
0.37577
0.41119
I. 96457
.61
.62
.63
5.0028
5.0531
5.1039
.19989
.19790
.19593
2.4015
2.4276
2.4540
2.6013
2.6255
2.6499 •
.92316
.92462
.92606
.69921
.70356
.70790
.38048
.38518
.38987
.41520
.41921
.42323
.96528
.96597
.96664
.64
.65
.66
5.1552
5.2070
5.2593
.19398
.19205
.19014
2.4806
2. 5075
2.5346
2.6746
2.6995
2.7247
.92747
.92886
.93022
.71224
.71659
.72093
.39456
.39923
.40391
.42725
.43129
.43532
.96730
.96795
,96858
.67
.68
.69
5.3122
5.3656
5.4195
.18825
.18637
.18452
2.5620
2.5896
2.6175
2.7502
2.7760
2.8020
.93155
.93286
.93415
.72527
.72961
.73396
.40857
.41323
.41788
.43937
.44341
.44747
.96921
.96982
.97042
.70
5.4739
.18268
2.6456
2.8283
.93541
0.73830
0.42253
0.45153
1.97100
.71
.72
.73
5.5290
5.5845
5.6407
.18087
.17907
.17728
2.6740
2.7027
2.7317
2,8549
2.8818
2.9090
.93665
.93786
.93906
.74264
.74699
.75133
.42717
.43180
.43643
.45559
.45966
.46374
.97158
.97214
.97269
.74
.75
.76
5.6973
5.7546
5.8124
.17552
.17377
.17204
2.7609
2.7904
2.8202
2.9364
2.9642
2.9922
.94023
.94138
.94250
.75567
. 76002
.76436
.44105
.44567
.45028
.46782
.47191
.47600
.97323
.97376
.97428
.77
.78
.79
5.8709
5.9299
5.9895
.17033
. 1 6864
.16696
2.8503
2. 8806
2.9112
3.0206
3.0492
3.0782
.94361
.94470
.94576
.76870
.77304
.77739
.45488
.45948
. 46408
.48009
.48419
.48830
.97479
.97529
.97578
1.80
6.0496
.16530
2.9422
8. 1075
.94681
0.78173
0.46867
0.49241
I. 97626
1-30
MATHEMATICS, UNITS, AND SYMBOLS
X
Natural Values
Common Logarithms
&
e~*
Sinh x
Cosh 3
Tanks
e?
Siuhz
Coshx
Tanha?
1.80
6.0496
.16530
2.9422
3.1075
.94681
0.78173
0.4686
0.4924
1.97626
.81
6 1104
.16365
2.9734
3.1371
.94783
.7860
.4732
.4965
.97673
*82
6"l719
.16203
3.0049
3.1669
.94884
.79042
.4778
.5006
.97719
!83
6.2339
.16041
3.0367
3.1972
.94983
.79476
.4824
.5047
.97764
84
6 2965
.15882
3.0689
3.2277
.95080
.79910
.4869
.5088
.97809
85
63598
.15724
3.1013
3.2585
.95175
. 80344
.49154
.51302
.97852
.86
6.4237
.15567
3.1340
3.2897
.95268
.80779
.49610
.51716
.97895
.87
6 4883
.15412
3.1671
3.3212
.95359
.81213
.50066
.52130
.97936
88
6*5535
.15259
3.2005
3.3530
.95449
.81647
.5052
.52544
.97977
.89
6,6194
.15107
3.2341
3.3852
.95537
.82082
.50976
.52959
.98017
.90
6.6859
.14957
3.2682
3.4177
.95624
0.82516
0.51430
0.53374
1.98057
.91
6.7531
.14808
3.3025
3.4506
.95709
.82950
.51884
.53789
.98095
92
6.8210
.14661
3.3372
3.4838
.95792
.83385
.52338
.54205
.98133
.93
6.8895
.14515
3.3722
3.5173
.95873
.83819
.52791
.54621
.98170
94
6.9588
.14370
3.4075
3.5512
.95953
. 84253
.53244
.55038
.98206
; .95
7.0287
.14227
3.4432
3.5855
.96032
.84687
.53696
.55455
.98242
.96
7.0993
.14086
3.4792
3.6201
.96109
.85122
.54148
.55872
.98272
.97
7.1707
. 13946
3.5156
3.6551
.96185
.85556
.54600
.56290
.98311
.98
7.2427
.13807
3.5523
3.6904
.96259
.85990
.55051
.56707
.98344
.99
7.3155
.13670
3.5894
3.7261
.96331
. 86425
.55502
.57126
.98377
2.00
7.3891
.13534
3.6269
3.7622
.96403
0.86859
0.55953
0.57544
1.98409
' 2.01
7.4633
.13399
3.6647
3.7987
.96473
.87293
.56403
. .57963
.98440
2.02
7.5383
. 13266
3.7028
3.8355
.96541
.87727
.56853
.58382
.98471
2.03
7.6141
.13134
3.7414
3.8727
.96609
.88162
.57303
.58802
.96502
2.04
7.6906
.13003
3.7803
3.9103
.96675
.88596
.57753
.59221
.98531
2.05
7.7679
.12873
3.8196
3.9483
.96740
.89030
.58202
.59641
.98560
2.06
7.8460
.12745
3.8593
3.9867
.96803
.89465
. 58650
.60061
.98589
2.07
7,9248
.12619
3.8993
4.0255
.96865
.89899
.59099
.60482
.98617
2.08
8.0045
.12493
3.9398
4.0647
.96926
. 90333
.59547
. 60903
.98644
2.09
8.0849
.12369
3.9806
4.1043
.96986
.90768
. 59995
.61324
.98671
2.10
8.1662
.12246
4.0219
4.1443
.97045
0.91202
0.60443
0.61745
1.98697
2.11
8.2482
.12124
4.0635
4.1847
.97103
.91636
. 60890
.62167
.98723
2.12
8.3311
.12003
4.1056
4.2256
.97159
.92070
.61337
.62589
.98748
2.13
8.4149
.11884
4. 1480
4.2669
.97215
.92505
.61784
.63011
.98773
2.14
8.4994
.11765
4.1909
4.3085
.97269
.92939
.62231
. 63433
. 98798
2.15
8.5849
.11648
4.2342
4.3507
.97323
.93373
. 62677
.63856
.98821
2.16
8.6711
.11533
4.2779
4.3932
.97375
.93808
.63123
.64278
.98845
2.T7
8.7583
.11418
4.3221
4.4362
.97426
.94242
.63569
.64701
.98868
2.18
8.8463
.11304
4.3666
4.4797
.97477
.94676
.64015
.65125
.98890
2.19
8.9352
.11192
4.4116
4.5236
.97526
.95110
.64460
. 65548
.98912
2.20
9.0250
.11080
4.4571
4.5679
.97574
0.95545
0.64905
0.65972
1.98934
2.21
9.1157
.10970
4.5030
4.6127
.97622
.95979
.65350
.66396
. 98955
2.22
9.2073
.10861
4.5494
4.6580
,97668
.96413
.65795
.66820
98975
2.23
9.2999
.10753
4.5962
4.7037
,97714
.96848
.66240
. 67244
.98996
2.24
9.3933
.10646
4.6434
4.7499
.97759
.97282
. 66684
. 67668
99016
2.25
2.26
9.4877
9.5831
.10540
.10435
4.6912
4.7394
4.7966
4.8437
.97803
.97846
.97716
.98151
.67128
.67572
. 68093
.68518
.99035
.99054
2.27
2.28
2.29
9.6794
9.7767
9.8749
. 10331
.10228
.10127
4.7880
4.8372
4.8868
4.8914
4.9395
4.9881
. 97888
. 97929
.97970
.98585
.99019
.99453
.68016
. 68459
.68903
.68943
. 69368
.69794
.99073
.99091
.99109
2.30
9.9742
.10026
4.9370
5.0372
.98010
0.99888
0.69346
0.70219
.99127
2.3t
2.32
2.33
10.074
10.176
10.278
.09926
.09827
.09730
4.9876
5.0387
5.0903
5.0868
5. 1370
5.1876
.98049
.98087
.98124
. 00322
.00756
.01191
.69789
. 70232
.70675
,70645
.71071
.71497
.99144
.99161
.99178
2.34
2.35
2.36
10.381
10.486
10.591
.09633
.09537
.09442
5.1425
5.1951
5.2483
5.2388
5.2905
5.3427
.98161
.98197
.98233
.01625
.02059
.02493
.71117
.71559
.72002
.71923
.72349
.72776
.99194
.99210
.99226
2.37
2.38
2.39
10.697
10.805
10.913
.09348
.09255
.09163
5.3020
5.3562
5.4109
5.3954
5.4487
5.5026
.98267
.98301
.98335
.02928
.03362
.03796
.72444
. 72885
. 73327
.73203
. 73630
.74056
.99241
.99256
.99271
1.40
U.Ott
.09072
5.4662
9.5569
.98367
.04231
.73769
.74484
.99285
EXPONENTIAL AND HYPERBOLIC TABLES
1-31
X
Natural Values
Common Logarithms
<P
e~x
Sinhz
Cosh a;
Tanhx
ex
Sinha;
Cosh a;
Tanha;
2.40
11.023
.09072
5.4662
5.5569
.98367
1.04231
0.73769
0.74484
1.99285
2.41
2.42
2.43
11.134
11.246
11.359
.08982
.08892
.08804
5.5221
5.5785
5.6354
5.6119
5.6674
5.7235
.98400
.98431
.98462
.04665
.05099
.05534
.74210
.74652
.75093
.74911
.75338
.75766
.99299
.99313
.99327
2.44
2.45
2.46
11.473
11.588
11.705
.08716
.08629
.08543
5.6929
5.7510
5.8097
5.7801
5.8373
5.8951
.98492
.98522
.98551
.05968
.06402
.06836
.75534
.75975
.76415
.76194
.76621
.77049
.99340
.99353
.99366
2.47
2.48
2.49
11.822
11.941
12.061
.08458
.08374
.08291
5.8689
5.9288
5.9892
5.9535
6.0125
6.0721
.98579
.98607
.98635
.07271
.07705
.08139
.76856
.77296
. 77737
.77477
.77906
.78334
.99379
.99391
.99403
2.50
12.182
.08208
6.0502
6.1323
.98661
1.08574
0.78177
0.78762
1.99415
2.51
2.52
2.53
12.305
12.429
12.554
.08127
.08046
.07966
6.1118
6.1741
6.2369
6.1931
6.2545
6.3166
.98688
.98714
.98739
.09008
.09442
.09877
.78617
. 79057
.79497
.79191
.79619
.80048
.99426
.99438
.99449
2.54
2.55
2.56
12.680
12.807
12.936
.07887
.07808
.07730
6.3004
6.3645
6.4293
6.3793
6. 4426
6.5066
.98764
.98788
.98812
.10311
.10745
.11179
.79937
.80377
.80816
.80477
.80906
.81335
.99460
.99470
.99481
2.57
2.58
2.59
13.066
13.197
13.330
.07654
.07577
.07502
6.4946
6.5607
6.6274
6.5712
6. 6365
6.7024
.98835
.98858
.98881
.11614
.12048
.12482
.81256
.81695
.82134
.81764
.82194
.82623
.99491
.99501
.99511
2.60
13.464
.07427
6.6947
6.7690
.98903
1.12917
0.82573
0.83052
1.99521
2.61
2.62
2.63
13.599
13.736
13.874
.07353
.07280
.07208
6.7628
6.8315
6.9008
6.8363
6.9043
6.9729
.98924
.98946
.98966
.13351
.13785
.14219
.83012
.83451
.83890
.83482
.83912
.84341
.99530
.99540
.99549
2.64
2.65
2.66
14.013
14.154
14.296
.07136
.07065
.06995
6.9709
7.0417
7.1132
7.0423
7. 1123
7.1831
.98987
.99007
.99026
.14654
.15088
.15522
. 84329
, 84768
. 85206
.84771
.85201
.85631
.99558
.99566
.99575
2.67
2.68
2.69
14.440
14.585
14.732
.06925
.06856
.06788
7.1854
7.2583
7.3319
7.2546
7.3268
7.3998
.99045
.99064
.99083
.15957
.16391
.16825
. 85645
. 86083
. 86522
.86061
.86492
.86922
.99583
.99592
.99600
2.70
14.880
.06721
7.4063
7.4735
.99101
1.17260
0.86960
0.87352
1.99608
2.71
2.72
2.73
15.029
15.180
15.333
.06654
.06587
.06522
7.4814
7.5572
7.6338
7.5479
7.6231
7.6991
.99118
.99136
.99153
.17694
.18128
.18562
. 87398
.87836
.88274
.87783
.88213
.88644
.99615
.99623
.99631
2.74
2.75
2.76
15.487
15.643
15.800
.06457
.06393
. 06329
7.7112
7.7894
7.8683
7.7758
7.8533
7.9316
.99170
.99186
.99202
.18997
.19431
.19865
.88712
.89150
. 89588
.89074
.89505
.89936
.99638
.99645
.99652
2.77
2.78
2.79
15.959
16.119
16.281
.06266
.06204
.06142
7.9480
8.0285
8.1098
8.0106
8.0905
8.1712
.99218
.99233
.99248
.20300
.20734
.21168
. 90026
. 90463
.90901
.90367
.90798
.91229
.99659
.99666
.99672
2.80
16.445
.06081
8.1919
8.2527
.99263
1.21602
0.91339
0.91660
1.99679
2.81
2.82
2.83
16.610
16.777
16.945
.06020
.05961
.05901
8.2749
8.3586
8.4432
8.3351
8.4182
8.5022
.99278
.99292
.99306
.22037
.22471
.22905
.91776
.92213
.92651
.92091
.92522
.92953
.99685
.99691
.99698
2.84
2.85
2.86
17.116
17.288
17.462
.05843
.05784
.05727
8.5287
8.6150
8.7021
8.5871
8.6728
8.7594
.99320
.99333
.99346
.23340
.23774
.24208
.93088
. 93525
.93963
.93385
.93816
.94247
.99704
.99709
.99715
2.87
2.88
2.89
17.637
17.814
17.993
. 05670
.05613
.05558
8.7902
8.8791
8.9689
8.8469
8.9352
9.0244
. 99359
.99372
.99384
.24643
.25077
.25511
. 94400
.94837
.95274
.94679
.95110
.95542
.99721
.99726
.99732
2.90
18.174
.05502
9.0596
9.1146
.99396
1.25945
0.95711
0.95974
T. 99737
2.91
2.92
2.93
18.357
18.541
18.728
.05448
.05393
.05340
9.1512
9.2437
9.3371
9.2056
9.2976
9.3905
.99408
.99420
.99431
.26380
.26814
.27248
.96148
.96584
.97021
.96405
.96837
. 97269
.99742
.99747
.99752
2.94
2.95
2.96
18.916
19.106
19.298
.05287
.05234
.05182
9.4315
9.5268
9.6231
9.4844
9.5791
9.6749
.99443
.99454
.99464
.27683
.28117
.28551
.97458
.97895
.98331
.97701
.98133
.98565
.99757
.99762
.99767
2.97
2.98
2.99
19.492
19.688
19.886
.05130
.05079
.05029
9.7203
9.8185
9.9177
9.7716
9.8693
9.9680
.99475
.99485
.99496
.28985
.29420
. 29854
.98768
.99205
.99641
.98997
.99429
,99861
.99771
.99776
.99780
3.00
20.086
.04979
10.018
10.068
.99505
1.30283
1.00078
1.00293
1.99785
1-32
MATHEMATICS, UNITS, AND SYMBOLS
EXPONENTIAL AND HYPERBOLIC TABLES
1-33
X
Natural Values
Common Logarithms
&
e~*
Sinha;
Cosh a;
Tanhrc
€*
Sinha
Cosh a;
Tanha:
3.60
36.598
.02732
18.285
18.313
.99851
1.56346
1.26211
1.26275
1.99935
3.61
3.62
3.63
36.966
37.338
37.713
.02705
.02678
.02652
18.470
18.655
18.843
18.497
18.682
18.870
.99854
.99857
.99859
.56780
.57215
.57649
.26646
.27080
.27515
.26709
.27143
.27576
.99936
.99938
.99939
3.64
3.65
3.66
38.092
38.475
38.861
.02625
.02599
.02573
19.033
19.224
19.418
19.059
19.250
19.444
.99862
.99865
.99868
,58083
.58517
.58952
.27950
.28385
.28820
.28010
.28444
.28878
.99940
.99941
.99942
3.67
3.68
3.69
39.252
39.646
40.045
.02548
.02522
.02497
19.613
19.811
20.010
19.639
19.836
20.035
.99870
.99873
.99875
.59386
.59820
.60255
.29255
.29690
.30125
.29311
.29745
.30179
.99944
.99945
.99946
3.70
40.447
.02472
20.211
20.236
.99878
1.60689
1.30559
1.30612
1.99947
3.71
3.72
3.73
40.854
41.264
41.679
.02448
.02423
.02399
20.415
20.620
20.828
20.439
20.644
20.852
. 99'880
.99883
.99885
.61123
.61558
.61992
.30994
.31429
.31864
.31046
.31480
.31914
.99948
.99949
.99950
3.74
3.75
3.76
42.098
42.521
42.948
.02375
.02352
.02328
21.037
21.249
21.463
21.061
21.272
21.486
.99887
.99889
.99892
.62426
.62860
.63295
.32299
.32733
.33168
.32348
.32781
,33215
.99951
.99952
.99953
3.77
3.78
3.79
43.380
43.816
44.256
.02305
.02282
.02260
21.679
21.897
22.117
21.702
21.919
22.140
.99894
.99896
.99898
.63729
.64163
.64598
.33603
.34038
.34472
.33649
.34083
.34517
.99954
.99955
.99956
3.80
44.701
.02237
22.339
22.362
.99900
1.65032
1.34907
1.34951
1.99957
3.81
3.82
3.83
45.150
45.604
46.063
.02215
.02193
.02171
22.564
22.791
23.020
22.586
22.813
23.042
.99902
.99904
.99906
.65466
.65900
.66335
.35342
.35777
.36211
\35384
.35818
.36252
.99957
.99958
.99959
3.84
3.85
3,86
46.525
46.993
47.465
.02149
.02128
.02107
23.252
23.486
23.722
23.274
23.507
23.743
.99908
.99909
.99911
.66769
.67203
.67638
.36646
.37081
.37515
.36686
.37120
.37554
.99960
.99961
.99961
3.87
3.88
3.89
47.942
48.424
48.911
.02086
.02065
.02045
23.961
24.202
24.445
23.982
24.222
24.466
.99913
.99915
.99916
.68072
.68506
.68941
.37950
.38385
.38819
.37988
.38422
.38856
.99962
.99963
.99964
3.90
49.402
.02024
24.691
24.711
.99918
1.69375
1.39254
1.39290
1.99964
3.91
3.92
3.93
49.899
50.400
50.907
.02004
.01984
.01964
24,939
25.190
25.444
24.960
25.210
25.463
.99920
.99921
.99923
.69809
.70243
.70678
.39689
.40123
.40558
.39724
.40158
.40591
.99965
.99966
.99966
3.94
3.95
3.96
51.419
51.935
52.457
.01945
.01925
.01906
25.700
25.958
26.219
25.719
25.977
26.238
.99924
.99926
.99927
.71112
.71546
.71981
.40993
.41427
.41862
.41025
.41459
.41893
.99967
.99968
.99968
3.97
3.98
3.99
52.985
53.517
54.055
.01887
.01869
.01850
26.483
26.749
27.018
26.502
26.768
27.037
.99929
.99930
.99932
.72415
.72849
.73284
.42296
.42731
.43166
.42327
.42761
.43195
.99969
.99970
.99970
4.00
54.598
.01832
27.290
27.308
.99933
1.73718
1.43600
1.43629
1.99971
4.01
4.02
4.03
55.147
55.701
56.261
.01813
.01795
.01777
27.564
27.842
28.122
27.583
27.860
28.139
.99934
.99936
.99937
.74152
.74586
.75021
.44035
.44469
.44904
.44063
.44497
.44931
.99971
.99972
.99973
4.04
4.05
4.06
56.826
57.397
57.974
.01760
.01742
.01725
28.404
28.690
28.979
28.422
28.707
28.996
.99938
.99939
.99941
.75455
.75889
.76324
.45339
.45773
.46208
.45365
.45799
.46233
. 99973
.99974
.99974
4.07
4.08
4.09
58.557
59.145
59.740
.01708
.01691
.01674
29.270
29.564
29.862
29.287
29.581
29.878
.99942
.99943
.99944
.76758
.77192
.77626
.46642
.47077
.47511
.46668
.47102
.47536
.99975
.99975
.99976
4.10
60.340
.01657
30.162
30.178
.99945
1.78061
1.47946
1,47970
1.99976
4.11
4.12
4.13
60.947
61.559
62.178
.01641
.01624
.01608
30.465
30.772
31.081
30.482
30.788
31.097
.99946
.99947
.99948
.78495
.78929
.79364
.48380
.48815
.49249
.48404
.48838
.49272
.99977
.99977
.99978
4.14
4.15
4.16
62.803
63.434
64.072
.01592
.01576
.01561
31-.393
31.709
32.028
31.409
31.725
32.044
.99949
.99950
.99951
.79798
.80232
.80667
.49684
.50118
.50553
.49706
.50140
.50574
.99978
.99978
.99979
4.17
4.18
4.19
64.715
65.366
66.023
.01545
.01530
.01515
32.350
32.675
33.004
32.365
32.691
33.019
.99952
.99953
.99954
.81101
.81535
.81969
.50987
.51422
.51856
.51008
.51442
.51876
.99979
.99980
.99980
4.20
66.686
.01500
33.336
33.351
.99955
1.82404
1.52291
1.52310
1.99980
1-34
MATHEMATICS, UNITS, AND SYMBOLS
X
Natural Values
Common Logarithms
<F
e-*
Sinks
Cosh s
Tanhre
e°
Sinha;
Cosh a;
Tanha:
4.20
66.686
.01500
33.336
33.35
.99955
1.82404
1.52291
1.52310
1.99980
4.21
67.357
.01485
33.67
33.68
.99956
.82838
.52725
.52745
.99981
4.22
68.033
.01470
34.009
34.02
.99957
.83272
.53160
.53179
.99981
4.23
68.717
.01455
34.351
34.36
.99958
.83707
.53594
.53613
.99982
4.24
69.408
.01441
34.697
34.71
.99958
.84141
.54029
.54047
.99982
4.25
70.105
.01426
35.046
35.060
.99959
.84575
.54463
.54481
.99982
4.26
70.810
.01412
35.398
35.412
.99960
.85009
.54898
.54915
.99983
4.27
71.522
.01398
35.754
35.768
.99961
. 85444
.55332
.55349
.99983
4.28
72.240
.01384
36.113
36.127
.99962
.85878
.55767
.55783
.99983
4.29
72.966
.01370
36.476
36.490
.99962
.86312
.56201
.56217
.99984
4.30
73.700
.01357
36.843
36.857
.99963
1.86747
1.66636
1.56652
1.99984
4.31
74.440
.01343
37.214
37.227
.99964
.87181
.57070
.57086
.99984
4.32
75.189
.01330
37.588
37.60
.99965
.87615
.57505
.57520
.99985
4.33
75.944
.01317
37.966
37.979
.99965
. 88050
.57939
.57954
.99985
4.34
76.708
.01304
38.347
38.360
.99966
. 88484
.58373
.58388
.99985
4.35
77.478
.01291
38.733
38.746
.99967
.88918
.58808
.58822
99986
4.36
78.257
.01278
39.122
39.135
.99967
.89352
.59242
.59256
.99986
4.37
79.044
.01265
39.515
39.528
.99968
. 89787
.59677
.59691
.99986
4.38
79.838
.01253
39.913
39.925
.99969
.90221
.60111
.60125
99986
4.39
80.640
.01240
40.314
40.326
.99969
.90655
.60546
.60559
.99987
4.40
81.451
.01228
40.719
40.732
.99970
1.91090
1.60980
1.60993
1.99987
4.47
4.42
4.43
82.269
83.096
83.931
.01216
.01203
.01191
41.129
41.542
41.960
41.141
41.554
41.972
.99970
.99971
.99972
.91524
.91958
.92392
.61414
.61849
.62283
.61427
.61861
. 62296
.99987
.99987
.99988
4.44
4.45
4.46
84.775
85.627
86.488
.01180
.01168
.01156
42.382
42.808
43.238
42.393
42.819
43.250
.99972
.99973
.99973
'.92827
.93261
. 93695
.62718
.63152
.63587
. 62730
. 63 1 64
. 63598
.99988
.99988
.99988
4.47
4.48
4.49
87.357
88.235
89.121
.01145
.01133
.01122
43.673
44.112
44.555
43.684
44.123
44.566
.99974
.99974
.99975
.94130
.94564
.94998
.64021
.64455
. 64890
. 64032
.64467
.64901
.99989
.99989
.99989
4.50
90.017
.01111
45.003
45.014
.99975 1.95433
1.65324
1.65335
1.99989
4.51
4.52
4.53
90. 922
91.836
92.759
.01100
.01089
.01078
45.455
45.912
46.374
45.466
45.923
46.385
.99976
.99976
.99977
. 95867
.96301
. 96735
.65759
.66193
. 66627
.65769
. 66203
. 66637
.99989
.99990
.99990
4.54
4.55
4.56
93.691
94.632
95.583
.01067
.01057
.01046
46.840
47.311
47.787
46.851
47.321
47.797
.99977
.99978
.99978
.97170
. 97604
.98038
. 67062
.67496
.67931
.67072
. 67506
.67940
. 99990
.99990
.99990
4.57
4.58
4.59
96.544
97.514
98.494
.01036
.01025
.01015
48.267
48.752
49.242
48.277
48.762
49.252
.99979
.99979
.99979
.98473
.98907
.99341
.68365
.68799
.69234
. 68374
.68808
.69243
.99991
.99991
.99991
4.60
99.484
.01005
49.737
49.747
.99980
1.99775
1.69668
1.69677
1.99991
4.61
4.62
4.63
100.48
101,49
02.51
.00995
.00985
.00975
50.237
50.742
51.252
50.247
50.752
51.262
.99980 2.00210
.99981 .00644
.99981 .01078
.70102
.70537
.70971
.70111
.70545
.70979
.99991
.99992
.99992
4.64
4.65
4.66
03.54
04.58
05.64
. 00966
.00956
.00947
51.767
52.288
52.813
51.777
52.297
52.823
.99981 .01513
.99982 .01947
.99982 .02381
.71406
.71840
.72274
.71414
.71848
.72282
.99992
.99992
.99992
4.67
4.68
4.69
06.70
07.77
08.85
.00937
.00928
.00919
53.344
53.880
54.422
53.354
53.890
54.431
.99982 .02816
.99983 .03250
.99983 .03684
.72709
.73143
.73577
.72716
.73151
.73585
.99992
.99993
.99993
4.70
109.95
.00910
54.969
54.978
.99983 2.04118
1.74012
1.74019
1.99993
4.71
4.72
4.73
11.05
12.17
13.30
.00900
.00892
.00883
55.522
56.080
56.643
55.531
56.089
56. 652
.99984 .04553
.99984 .04987
.99984 .05421
.74446
.74881
.75315
. 74453
. 74887
.75322
.99993
.99993
. 99993
4.74
4.75
4.76
14.43
15.58
16.75
.00874
.00865
.00857
57.213
57.788
58.369
57.222
57.796
58.377
.99985 .05856-
.99985 .06290
.99985 .06724
.75749
.76184
.76618
.75756
.76190
. 76624
.99993
.99993
.99994
4.77
4.78
4.79
17.92
19.10
20.30
.00848
.00840
.00831
58.955
59.548
60.147
58.964
59.556
60.155
99986 .07158
99986 .07593
99986 .08027
.77052
.77487
.77921
.77059
.77493
.77927
.99994
.99994
.99994
4.80
121.51
.00823
60.751
60.759
99986 2.08461
1.78355
1.78361 i
L. 99994
EXPONENTIAL AND HYPERBOLIC TABLES
1-35
X
Natural Values]
Common Logarithms
e*
e-s
Sinho;
Cosh a;
Tauhs
«*
Sinhs
Cosh a;
Tanh x
4.80
121.51
.00823
60.751
60.760
.99986
2.08461
1.78355
1.78361
1.99994
4.81
4.82
4.83
122.73
123.97
125.21
.00815
.00807
.00799
61.362
61.979
62.601
61.370
61.987
62.609
.99987
.99987
.99987
.08896
.09330
.09764
.78790
.79224
.79658
.78796
.79230
.79664
.99994
.99994
.99994
4.84
4.85
4.86
126.47
127.74
129.02
.00791
.00783
.00775
63.231
63.866
64.508
63.239
63.874
64.516
.99987
.99988
.99988
.10199
.10633
.11067
.80093
.80527
.80962
.80098
.80532
.80967
.99995
.99995
.99995
4.87
4.88
4.89
130.32
131.63
132.95
.00767
.00760
,00752
65.157
65.812
66.473
65.164
65.819
66.481
.99988
.99988
.99989
.11501
.11936
.12370
.81396
.81830
.82265
.81401
.81835
.82269
.99995
.99995
.99995
4.90
134.29
.00745
67.141
67.149
.99989
2.12804
1.82699
1.82704
1.99995
4.91
4.92
4.93
135.64
137.00
138.38
.00737
.00730
.00723
67.816
68.498
69.186
67.823
68.505
69.193
.99989
.99989
.99990
.13239
.13673
.14107
.83133
.83568
.84002
.83138
.83572
.84006
.99995
.99995
.99995
4.94
4.95
4.96
139.77
141.17
142.59
.00715
.00708
.00701
69.882
70.584
71.293
69.889
70.591
71.300
.99990
.99990
.99990
.14541
.14976
.15410
.84436
.84871
.85305
.84441
.84875
.85309
.99996
.99996
,99996
4.97
4.98
4.99
144.03
145.47
146.94
.00694
.00687
.00681
72.010
72.734
73.465
72.017
72.741
73.472
.99990
.99991
.99991
.15844
.16279
.16713
.85739
.86174
.86608
.85743
.86178
.86612
.99996
.99996
.99996
6.00
148.41
.00674
74.203
74.210
.99991
2.17147
1.87042
1.87046
1.99996
5.01
5.02
5.03
149.90
151.41
152.93
.00667
.00660
.00654
74.949
75.702
76.463
74.956
75.710
76.470
.99991
.99991
.99991
.17582
.18016
.18450
.87477
.87911
.88345
.87480
.87915
.88349
.99996
.99996
.99996
5.04
5.05
5.06
154.47
156.02
157.59
.00647
.00641
.00635
77.232
78.008
78.792
77.238
78.014
78.798
.99992
.99992
.99992
.18884
.19319
.19753
.88780
.89214
.89648
.88783
.89217
.89652
.99996
.99996
.99997
5.07
5.08
5.09
159.17
160.77
162.39
.00628
.00622
.00616
79.584
80.384
81.192
79.590
80.390
81.198
.99992
.99992
.99992
.20187
.20622
.21056
.90083
.90517
.90951
.90086
.90520
.90955
.99997
.99997
.99997
6.10
164.02
.00610
82.008
82.014
.99993
2.21490
1.91386
1.91389
1.99997
5.11
5.12
5.13
165.67
167.34
169.02
.00604
.00598
.00592
82.832
83.665
84.506
82.838
83.671
84.512
.99993
.99993
.99993
.21924
.22359
.22793
.91820
.92254
.92689
.91823
.92257
.92692
.99997
.99997
.99997
5.14
5.15
5.16
170.72
172.43
174.16
.00586
.00580
.00574
85.355
86.213
87.079
85.361
86.219
87.085
.99993
.99993
.99993
.23227
.23662
.24096
.93123
.93557
.93992
.93126
.93560
.93994
.99997
.99997
.99997
5.17
5.18
5.19
175.91
177.68
179.47
.00568
.00563
.00557
87.955
88.839
89.732
87.960
88.844
89.737
.99994
.99994
.99994
.24530
.24965
.25399
.94426
.94860
.95294
.94429
.94863
.95297
.99997
.99997
.99997
6.20
181.27
.00552
90.633
90.639
.99994
2.25833
1.95729
1.95731
1.99997
5.21
5.22
5.23
183.09
184.93
186.79
.00546
.00541
.00535
91.544
92.464
93.394
91.550
92.470
93.399
.99994
.99994
.99994
.26267
.26702
.27136
.96163
.96597
.97032
.96166
.96600
.97034
.99997
.99997
.9999e
5.24
5.25
5.26
188.67
190.57
192.48
.00530
.00525
.00520
94,332
95.281
96.238
94.338
95.286
96.243
.99994
.99994
.99995
.27570
.28005
.28439
.97466
.97900
.98335
.97469
.97903
.98337
.99998
.99998
.99998
5.27
5.28
5.29
194.42
196.37
198.34
.00514
.00509
.00504
97.205
98.182
99.169
97.211
98.188
99.174
.99995
.99995
.99995
.28873
.29307
.29742
.98769
.99203
.99638
.98771
.99206
.99640
.99998
,99998
.99998
6.30
200.34
.00499
100.17
100.17
.99995
2.30176
2.00072
2.00074
1.99998
5.31
5.32
5.33
202.35
204.38
206.44
.00494
.00489
.00484
101.17
102.19
103.22
101.18
102.19
103.22
.99995
.99995
,99995
.30610
.31045
.31479
.00506
.00941
.01375
.00508
.00943
.01377
.99998
.99998
.99998
5.34
5.35
5.36
208.51
210.61
212.72
.00480
.00475
.00470
104.25
105.30
106.36
104.26
105.31
106.36
.99995
.99995
.99996
.31913
.32348
.32782
.01809
.02244
.02678
.01811
.02246
.02680
.99998
.99998
.99998
5.37
5.38
5.39
214.86
217.02
219.20
.00465
.00461
.00456
107.43
108.51
109.60
107.43
108.51
109.60
.99996
.99996
.99996
.33216
.33650
.34085
.03112
.03547
.03981
.03114
.03548
.03983
.99998
.99998
,99998
6.40
221.41
.00452
110.70
110.71
.99996
2.34519
2.04415
2.04417
1.99998
1-36
MATHEMATICS, UNITS, AND SYMBOLS
X
_. Natural Values
Common Logarithms
«*
«-*
Sinhx
Cosh a;
Tanks
e*
Sinha;
Cosh x
Tanhx
5.40
221.41
.00452
110.70
110.71
.99996
2.34519
2.04415
2.04417
1.99998
5.41
5.42
5.43
223.63
225.88
228.15
.00447
.00443
.00438
111.81
112.94
114.07
111.82
112.94
114.08
.99996
.99996
.99996
.34953
.35388
.35822
.04849
.05284
.05718
.04851
.05285
.05720
.99998
.99998
.99998
5.44
5.45
5.46
230.44
232.76
235.10
.00434
.00430
.00425
115.22
116.38
117.55
115.22
116.38
117.55
.99996
.99996
.99996
.36256
.36690
.37125
.06152
.06587
.07021
.06154
.06588
.07023
.99998
.99998
.99998
5.47
5.48
5.49
237.46
239. 85
242.26
.00421
.00417
.00413
118.73
119.92
121.13
118.73
119.93
121.13
.99996
.99997
.99997
.37559
.37993
.38428
.07455
.07890
.08324
.07457
.07891
.08325
.99998
.99998
.99999
6.60
244.69
.00409
122.34
122.35
.99997
2.38862
2.08758
2.08760
1.99999
5.51
5.52
5.53
247.15
249.64
252. 14
.00405
.00401
.00397
123.57
124.82
126.07
123.58
124.82
126.07
.99997
.99997
.99997
.39296
.39731
.40165
.09193
.09627
.10061
.09194
.09628
.10063
.99999
.99999
.99999
5.54
5.55
5.56
254.68
257.24
259.82
.00393
.00389
.00385
127.34
128.62
129.91
127.34
128.62
129.91
.99997
.99997
.99997
.40599
.41033
.41468
.10495
.10930
.11364
.10497
.10931
.11365
.99999
.99999
.99999
5.57
5.58
5.59
262.43
265.07
267.74
.00381
.00377
.00374
131.22
132.53
133.87
131.22
132.54
133.87
.99997
.99997
.99997
.41902
.42336
.42771
.11798
.12233
.12667
.11800
.12234
.12668
.99999
.99999
.99999
6.60
270.43
.00370
135.21
135.22
.99997
2.43205
2.13101
2.13103
1.99999
5.61
5.62
5.63
273.14
275.89
278. 66
.00366
.00362
.00359
136.57
137.94
139.33
136.57
137.95
139.33
.99997
.99997
.99997
.43639
.44074
.44508
.13536
.13970
.14404
.13537
.13971
.14405
.99999
.99999
.99999
5.64
5.65
5.66
281.46
284.29
287.15
.00355
.00352
.00348
140.73
142.14
143.57
140.73
142.15
143.58
.99997
.99998
.99998
.44942
.45376
.45811
.14839
.15273
.15707
.14840
.15274
.15708
.99999
.99999
.99999
5.67
5.68
5.69
290.03
292. 95
295. 89
.00345
.00341
,00338
145.02
146.47
147.95
145.02
146.48
147.95
.99998
.99998
.99998
,46245
.46679
.47114
.16141
.16576
.17010
.16142
.16577
.17011
.99999
.99999
.99999
6.70
298.87
.00335
149.43
149.44
.99998
2.47548
2.17444
2.17445
1.99999
5.71
5.72
5.73
301.87
304.90
307.97
.00331
.00328
.00325
150.93
152.45
153.98
150.94
152.45
153.99
.99998
.99998
.99998
.47982
.48416
.48851
.17879
.18313
.18747
.17880
.18314
.18748
.99999
.99999
.99999
5.74
5.75
5.76
311.06
314.19
317.35
.00321
.00318
.00315
155.53
157.09
158.67
155.53
157.10
158.68
.99998
.99998
.99998
.49285
.49719
.50154
.19182
.19616
.20050
.19182
.19617
.20051
.99999
.99999
.99999
5.77
5.78
5.79
320.54
323.76
327.01
.00312
.00309
.00306
160.27
161.88
163.51
160.27
161.88
163.51
.99998
.99998
.99998
.50588
.51022
.51457
.20484
.20919
.21353
.20485
.20920
.21354
.99999
.99999
.99999
6.80
330.30
.00303
165.15
165.15
.99998
2.51891
2.21787
2.21788
I. 99999
5.81
5.82
5.83
333.62
336.97
340.36
.00300
.00297
.00294
166.81
168.48
170.18
166.81
168.49
170.18
.99998
.99998
.99998
.52325
.52759
.53194
.22222
.22656
.23090
.22222
.22657
.23091
.99999
.99999
.99999
5.84
5.85
5.86
343.78
347.23
350.72
.00291
.00288
.00285
171.89
173.62
175.36
171.89
173.62
175.36
.99998
.99998
.99998
.53628
.54062
.54497
.23525
.23959
.24393
.23525
.23960
.24394
.99999
.99999
.99999
5.87
5.88
5.89
354.25
357.81
361.41
.00282
.00279
.00277
177.12
178.90
180.70
177.13
178.91
180.70
.99998
.99998
.99998
.54931
.55365
.55799
.24828
.25262
.25696
.24828
. 25262
.25697
.99999
.99999
.99999
6.90
366.04
.00274
182.52
182.52
.99998
2.56234
2.26130
2.26131
1.99999
5.91
5.92
5.93
368.71
372.41
376.15
.00271
.00269
.00266
184.35
186.20
188.08
184.35
186.21
188.08
.99999
.99999
.99999
.56668
.57102
.57537
.26565
.26999
.27433
.26565
.27000
. 27434
.99999
.99999
.99999
5.94
1 5.95
5.96
379.93
383.75
387. 61
.00263
.00261
.00258
189.97
191.88
193.80
189.97
191.88
193.81
.99999
.99999
.99999
.57971
.58405
.58840
.27868
.28302
.28736
. 27868
. 28303
. 28737
.99999
.99999
.99999
5.97
5.98
5.99
391.51
395.44
399.41
.00255
.00253
.00250
195.75
197.72
199.71
195.75
197,72
199.71
.99999
.99999
.99999
.59274
.59708
.60142
.29171
.29605
.30039
.29171
.29605
.30040
.99999
.99999
.99999
6.00
403.43
.00248
201.71
201.72
.99999
2.60577
2.30473
2.30474
.99999
TRANSMISSION UNIT AND POWER REFERENCE LEVELS 1-37
14. BESSEL FUNCTIONS
The chart below shows approximate values for some representative Bessel functions of
the first kind. Values for higher-order Bessel functions can be computed by successive
application of the recurrence formula
starting with the values of JQ(X) and J\(x).
1.0
-0.5
FIG. 1. Chart of Bessel Functions.
16. TRANSMISSION UNIT AND POWER REFERENCE
LEVELS.— DECIBELS
Power losses occur in all parts of an electric circuit; in many circuits, which are built
up of a number of components, the easiest method of predicting overall efficiencies is to
determine individual efficiencies and combine them. When amplifiers are used, power
gains exist (as far as the alternating signal current is concerned) and must be considered.
For, although the useful power is less than the total power input, the output signal power
may be greater than the input signal power, so that, using the conventional definition of
efficiency, values greater than 100 per cent can be obtained.
THE DECIBEL AND THE NEPER. In order to avoid the multiplication of the indi-
vidual efficiencies recourse has been had to logarithms of the efficiencies, giving measures
of efficiency which can be added and subtracted directly.
Many units have been proposed and several have at various times been adopted in dif-
ferent localities. At the present time two such units are in general use in Europe and this
country, one based on the napierian system of logarithms, the other based on the decimal
system of logarithms. The International Advisory Committee on Long Distance Telephony
of Europe has recommended that both these units be standardized and defined as follows:
The unit of transmission expresses the ratio of apparent or real power in transmission
systems. In practice, the number of units of transmission in a given case is expressed in
terms of a logarithm.
In the case of two powers Pi and Pz the number of units is :
•p
in the napierian system, 1/2 loge —
in the decimal system,
10810
The napierian unit is called the neper. The decimal unit is called the bel.
submultiple of these units may be used, as decineper and decibel.
A decimal
1-38 MATHEMATICS, UNITS, AND SYMBOLS
The unit generally used in this country is the decibel, which is exactly equivalent to
and was first standardized as the "transmission unit"; it is also exactly equivalent to
the "sensation unit" used in acoustic work. The decibel is abbreviated db, the trans-
mission unit TU, and the sensation unit SU. The neper is called the (31 unit. The com-
parative sizes of the two units is given by the fact that
logc ^ = 2.3026 logio p^ ,
so that 0.8686 neper is equal to 1 bel. Also 1 neper = 11.51 decibels.
From the above definition the number of decibels which expresses the ratio between
any two powers is
N = 10 logio ™
The quantity N is called the transmission equivalent of the element considered. It may
be readily evaluated for a particular ratio by multiplying the common logarithm of this
ratio by 10. If Pi represents the delivered power and p2 the input power, N will be nega-
tive for power losses and positive for power gains, since the logarithms of numbers less
than unity are negative.
The use of the decibel may be seen from the following. If two circuit elements, with a
•n Tp
ratio of power output to power input of ~ and ~ , respectively, are connected in series,
the power ratio of the combination is
Pout _ PI Pa
Pin ~ P2 P4 !
where NI and N2 are the transmission equivalents of the first and second elements, respec-
tively. Taking the logarithms of both sides and multiplying through by 10,
10 log -rr— — = NI -}- Nz — NT
•P in
It is thus seen that any number of transmission equivalents can be added (losses with
their associated minus sign) to obtain the transmission equivalent of a complete circuit.
In making measurements of circuit efficiency the current ratio, or the voltage ratio,
is usually more readily obtainable than the power ratio. Either of these ratios may bo
used to specify the efficiency of the circuit when conditions are such that it is the square
root of the power ratio.
In this case Ji2 _ Pi
and taking the square root of both sides
By the method used above in the case of power ratios, the transmission equivalent is
N = 20 logio 7-1 = 20 logic, ~
1 z J&z ~
It must be remembered that this is true only when the current or voltage ratio is the square root
of the power ratio, the simplest case being where the currents through, or voltages across,
equal impedances are measured.
LOGARITHMIC VOLTAGE RATIO. In measuring electron-tube amplifiers, it is fre-
quently useful to measure the voltage gain of each stage and compare the sum with the
overall gain of the complete amplifier. Such measurements are in many cases conveniently
made in terms of voltage and are made only with great difficulty in terms of power. The
habit has grown up of using the advantages of logarithmic addition and calibrating ampli-
fiers in terms of comparison voltages without any regard for the impedance relations.
Furthermore in some instances the overall sensitivity of amplifiers and complete radio
sets has frequently been expressed in terms of "decibels below 1 volt" with no thought of
impedance. According to the above discussion this, of course, is a misuse of the term.
Since it is so convenient, however, it is a practice which is likely to continue. Confusion
can be avoided by the association of a new term to this measurement. It has been sug-
gested that the abbreviation dbv be used to indicate that the logarithmic ratios are in
terms of volts and not in terms of power. It has furthermore been suggested that the
dbv also carry the implication where appropriate that it is below the level of 1 volt. A
TRANSMISSION UNIT AND POWER REFERENCE LEVELS 1-39
Decibels Versus Power, Voltage, and Current Ratios
db
Current and
Voltage Ratio
Power Ratio
db
Current and
Voltage Ratio
Power Ratio
Gain
Loss
Gain
Loss
Gain
Loss
Gain
Loss
0.1
.012
0.9886
.023
0.9772
5.6
1.905
0.5248
3.631
0.2754
0.2
.023
.9772
.047
.9550
5.7
1.928
.5188
3.715
.2692
0.3
.035
.9661
.072
.9333
5.8
1.950
.5129
3.802
.2630
0.4
.047
.9550
.097
.9120
5.9
1.973
.5070
3.891
.2570
0.5
.059
.9441
.122
.8913
6.0
1.995
.5012
3.981
.2512
0.6
.072
.9333
.148
.8710
6.1
2.018
.4958
4.074
.2455
0.7
.084
.9226
.175
.8511
6.2
2.042
.4898
4.169
.2399
0.8
.097
.9120
.202
.8318
6.3
2.065
.4842
4.266
.2344
0.9
.109
.9016
.230
.8128
6.4
2.089
.4786
4.365
.2291
1.0
.122
.8913
.259
.7943
6.5
2.114
.4732
4.467
.2239
.1
.135
.8811
.288
.7763
6.6
2.138
.4677
4.571
.2188
.2
.148
.8710
.318
.7586
6.7
2.163
.4624
4.677
.2138
.3
.162
.8610
.349
.7413
6.8
2.188
.4571
4.786
.2089
.4
.175
.8511
.380
.7244
6.9
2.213
.4519
4.898
.2042
' .5
.189
.8414
.413
.7080
7.0
2.239
.4467
5.012
.1995
.6
.202
.8318
.445
.6918
7.1
2.265
.4416
5.129
.1950
.7
.216
.8222
.479
.6761
7.2
2.291
.4365
5.248
.1906
.8
.230
.8128
.514
.6607
7.3
2.317
.4315
5.370
.1862
.9
.245
.8035
.549
.6457
7.4
2.344
.4266
5.495
.1820
2.0
.259
.7943
.585
.6310
7.5
2.371
.4217
5.623
.1778
2.1
.274
.7852
.622
.6166
7.6
2.399
.4169
5.754
.1738
2.2
.288
.7763
.660
.6026
7.7
2.427
.4121
5.888
.1698
2.3
.303
.7674
.698
.5888
7.8
2.455
.4074
6.026
.1660
2.4
.318
.7586
.738
.5754
7.9
2.483
.4027
6. 166
.1622
2.5
.334
.7499
.778
.5623
8.0
2.512
.3981
6.310
.1585
2.6
.349
.7413
.820
.5495
8.1
2.541
.3936
6.457
.1549
2.7
.365
.7328
.862
.5370
8.2
2.570
.3891
6.607
.1514
2.8
.380
.7244
.905
.5248
8.3
2.600
.3846
6.761
.1479
2.9
.396
.7161
1.950
.5129
8.4
2.630
.3802
6.918
.1445
3.0
.413
.7080
1.995
.50'! 2
8.5
2.661
.3758
7.079
.1413
3.1
.429
.6998
2.042
.4898
8.6
2.692
.3715
7.244
.1380
3.2
.445
.6918
2.089
.4786
8.7
2.723
.3673
7.413
.1349
3.3
.462
.6839
2.138
.4677
8.8
2.754
.3631
7.586
.1318
3.4
.479
.6761
2.188
.4571
8.9
2.786
.3589
7.762
.1288
3.5
.496
.6683
2.239
.4467
9.0
2.818
.3548
7.943
.1259
3.6
.514
.6607
2.291
.4365
9.1
2.851
.3508
8.128
.1230
3.7
.531
.6531
2.344
.4266
9.2
2.884
.3467
8.318
.1202
3.8
.549
.6457
2.399
.4169
9.3
2.917
.3428
8.511
.1175
3.9
.567
.6383
2.455
.4074
9.4
2.951
.3389
8.710
.1148
4.0
.585
.6310
2.512
.3981
9.5
2.985
.3350
8.913
.1122
4.1
.603
.6237
2.570
.3891
9.6
3.020
.3311
9.120
.1097
4.2
.622
.6166
2.630
.3802
9.7
3.055
.3273
9.333
.1072
4.3
.641
.6095
2.692
.3715
9.8
3.090
.3236
9.550
.1047
4.4
.660
.6026
2.754
.3631
9.9
3.126
.3199
9.772
.1023
4.5
.679
.5957
2*818
.3548
10.0
3.162
.3162
10.000
.1000
4.6
.698
.5888
2.884
.3467
10.1
3.199
.3126
10.23
.0977
4.7
.718
.5821
2.951
.3389
10.2
3.236
,3090
10.47
.0955
4.8
.738
,5754
3.020
.3311
10.3
3.273
.3055
10.72
.0933
4.9
.758
.5689
3.090
.3236
10.4
3.311
.3020
10.97
.0912
5.0
.778
.5623
3.162
.3162
10.5
3.350
.2985
11.22
.0891
5.1
.799
.5559
3.236
.3090
10.6
3.388
.2951
11.48
.0871
5.2
.820
.5495
3.311
.3020
10.7
3.428
.2917
11.75
.0851
5.3
.841
.5433
3.388
.2951
10.8
3.467
.2884
12.02
.0832
5.4
.862
.5370
3.467
.2884
10.9
3.508
.2851
12.30
.0813
5.5
.884
.5309
3.548
.2818
11.0
3.548
.2818
12.59
.0794
1-40 MATHEMATICS, UNITS, AND SYMBOLS
Decibels Versus Power, Voltage, and Current Ratios — Continued
db
Current and
Voltage Ratio
Power Ratio
db
Current and
Voltage Ratio
Power Ratio
Gain
Loss
Gain
Loss
Gain
Loss
Gain
Loss
11.1
3.589
0.2786
12.88
0.0776
16.1
6.383
0.1566
40.74
0.0245
11.2
3.631
.2754
13.18
.0759
16.2
6.457
.1549
41.69
.0239
11.3
3.673
.2723
13.49
.0741
16.3
6.531
.1531
42.66
.0234
11.4
3.715
.2692
13.81
.0724
16.4
6.607
.1514
43.65
.0229
11.5
3.758
.2661
14.13
.0708
16.5
6.683
.1496
44.67
.0224
11.6
3.802
.2630
14.45
.0692
16.6
6.761
.1479
45.71
.0219
11.7
3.846
.2600
14.79
.0676
16.7
6.839
.1462
46.77
.0214
11.8
3.891
.2570
15.14
.0661
16.8
6.918
.1445
47.86
.0209
11.9
3.936
.2541
15.49
.0646
16.9
6.998
.1429
48.98
.0204
12.0
3.981
.2512
15.85
.0631
17.0
7.079
.1413
50.12
.0200
12.1
4.027
.2483
16.22
.0617
17.1
7.161
.1396
51.29
.0195
12.2
4.074
.2455
16.60
.0603
17,2
7.244
.1380
52.43
.0191
12.3
4.121
.2427
16.98
.0589
17.3
7.328
.1365
53.70
.0186
12.4
4.169
.2399
17.38
.0575
17.4
7.413
.1349
54.96
.0182
12.5
4.217
.2371
17.78
.0562
17.5
7.499
.1334
56.23
.0178
12.6
4.266
.2344
18.20
.0550
17.6
7.586
.1318
57.54
.0174
12.7
4.315
.2317
18.62
.0537
17.7
7.674
.1303
58.88
.0170
12.8
4.365
.2291
19.05
.0525
17.8
7.762
.1288
60.26
.0166
12.9
4.416
.2265
19.50
.0513
17.9
7.852
.1273
61.66
.0162
13.0
4.467
.2239
19.95
.0501
18.0
7.943
.1259
63.10
.0158
13.1
4.519
.2213
20.42
.0490
18.1
8.035
.1245
64.57
.0155
13.2
4.571
.2188
20.89
.0479
18.2
8.128
.1230
66.07
.0151
13.3
4.624
.2163
21.38
.0468
18.3
8.222
.1216
67.61
.0148
13.4
4.677
.2138
21.88
.0457
18.4
8.318
.1202
69.18
.0145
13.5
4.732
.2113
22.39
.0447
18.5
8.414
.1189
70.80
.0141
13.6
4.786
.2089
22.91
.0437
18.6
8.511
.1175
72.44
.0138
13.7
4.842
.2065
23.44
.0427
18.7
8.610
.1161
74.13
.0135
13.8
4.898
.2042
23.99
.0417
18.8
8.710
.1148
75.86
.0132
13.9
4.955
.2018
24.55
.0407
18.9
8.811
.1135
77.63
,0129
14.0
5.012
.1995
25.12
.0398
19.0
8.913
.1122
79.43
.0126
14.1
5.070
.1972
25.70
.0389
19.1
9.016
.1109
81.28
,0123
14.2
5.129
.1950
26.30
.0380
19.2
9.120
.1097
83.18
.0120
14.3
5.188
,1928
26.92
.0372
19.3
9.226
.1084
85.11
.0117
14.4
5.248
.1906
27.54
.0363
19.4
9.333
.1072
87.10
.0115
14.5
5.309
.1884
28.18
.0355
19.5
9.441
.1059
89,13
.0112
14.6
5.370
.1862
28.84
.0347
19.6
9.550
.1047
91.20
.0110
14.7
5.433
.1841
29.51
.0339
19.7
9.661
,1035
93.33
.0107
14.8
5.495
.1620
30.20
.0331
19.8
9.772
.1023
95.50
.0105
14.9
5.559
.1799
30.90
.0324
19.9
9.886
.1012
97.72
,0102
15.0
5.623
.1778
31.62
.0316
20.0
10.000
.1000
100.0
.0100
15.1
5.689
.1758
32.36
.0309
30.0
31.62
.0316
1,000
.0010
15.2
5.754
.1738
33.11
.0302
40.0
100.0
.0100
104
10-4
15.3
5.821
.1718
33.88
.0295
50.0
316.2
.0032
105
10-5
15.4
5.888
.1698
34.67
.0288
60.0
1,000.0
.0010
108
10-8
15.5
5.957
.1679
35.48
.0282
70.0
3f162.*0
.0003
107
10-7
15.6
6.026
.1660
36.31
.0275
80.0
0,000.0
.0001
108
10-8
15.7
6.096
,1641
37.15
.0269
90.0
1,620.0
.00003
109
10-9
15.8
6.166
.1622
38.02
.0263
100.0
00,000,0
.00001
15.9
6.237
,1603
38.91
,0257
16.0
6.310
.1585
39.81
.0251
BIBLIOGRAPHY 1-41
sensitivity of 100 AIV could be expressed as —80 dbv, and a sensitivity of 10 iiv as — 100
dbv, with this system.
A table is appended giving values of transmission equivalents in terms of both power
and current, or voltage, ratios in tenths of a decibel up to 20 db. For values above 20 db
the tables may be used as described below.
Example. To find the current and power ratios for a loss of 57.6 db.
1. The power ratio of 50 db is 10~5 (this being the first power ratio which is an even
submultiple of 10 and corresponds to less than 57.6 db).
2. The power ratio of 7.6 (57.6 - 50 = 7.6) db is 0.1738.
3. To add decibels, power ratios must be multiplied, hence:
Power ratio of 57.6 db = 0.1738 X 10~5
4. The current ratio of 40 db is 0.01 (first current ratio which is an even submultiple
of 10 and corresponds to less than 57.6 db) .
5. The current ratio of 17.6 (57.6 - 40 = 17.6) db is 0.1318.
6. Multiplying these ratios:
Current ratio of 57.6 db = 0.001318
POWER REFERENCE LEVELS. When the efficiency of a device or system is ex-
pressed in decibels there is in general no indication of the actual amount of power in the
device. In comparing devices it is frequently desirable to know the actual overall effi-
ciency. In such a case this can readily be expressed in decibels, 100 per cent efficiency
being represented by zero decibels. In many cases, however, it is more desirable that the
relative efficiencies at different frequencies be known ; in some such cases it is also desirable
that the normal power capacity of the device be specified in such form as to be readily
comparable with similar devices.
For such a specification to be made when the ordinates of a characteristic are in deci-
bels, it is only necessary to specify some arbitrary amount of power as corresponding to
zero decibels; then every value of decibels represents a definite amount of power (or vol-
ume level). The amount of power chosen as the reference level is completely arbitrary;
hence it has been customary to choose some average value of power as zero level, for a
particular type of work.
Attempts at standardization have been made, with the result that the American Stand-
ards Association (and IRE) has recommended 1 milliwatt in 600 ohms in connection with
a particular meter to measure levels in radio program transmission (see ASA "American
Recommended Practice for Volume Measurements of Electrical Speech and Program
Waves," Nov. 6, 1942) and has introduced the term vu (vee-you) to represent the number
of decibels above or below this level. Also it has become customary to specify power in
dbm which is used to mean decibels above or below 1 milliwatt.
However, some other groups are still using other levels. For instance, in sound-motion
pictures the reference level is 6 milliwatts. Also certain radar engineers use decibels below
or above 1 watt.
It will apparently require further action by the American Standards Association to bring
order out of the present chaos. The desirability of such a standard is shown by the expe-
rience in the acoustic field where 10 ~16 watt per sq cm was universally adopted, so that
measurements made anywhere are everywhere intelligible. Until the adoption of such a
standard, great care must be exercised in comparing curves and statements of levels to
insure that correction is made for differences in reference levels. Also a statement of the
reference used should always be included as a part of any publication of results.
BIBLIOGRAPHY
Hilliard, J. K., Definition of Standard Reference Systems, Electronics, Vol. 3, 192 (November 1931).
Martin, W. H., Decibel — The Name for the Transmission Unit, B.S.T.J., Vol. 8, 1 (January 1929).
Martin, W. H., and C. H. G. Gray. Master Reference System for Telephone Transmission. B.S.T.J.,
Vol. 8, 536 (July 1929).
1-42 MATHEMATICS, UNITS, AND SYMBOLS
UNITS AND CONVERSION FACTORS
By J. G. Brainerd and Carl C. Chambers
16. SYSTEMS OF UNITS
The magnitude of a physical quantity has no tangible meaning except as the relative
magnitude of that quantity as compared with some other quantity of the same nature.
Thus, 50 ohms is a resistance having a magnitude 50 times the resistance of 1 ohm. There-
fore, whenever it is necessary or desirable to talk about the magnitude of a physical^
quantity, it is necessary to have a basis for comparison. This basis for a quantity is
called the unit of magnitude of that quantity. In order to communicate the idea of
magnitude between different people, it is necessary that they at least know the relative
magnitudes of their units. It is the purpose of this section to act as tool for the specifica-
tion of the relative magnitudes of the more commonly used systems of units for physical
quantities.
Because of the relations denning physical laws, there are relations between the magni-
tudes of physical quantities. It is desirable that these physical relations be expressed
alike hi the different systems of units. For instance, the relation mass X acceleration
= force should be independent of the system of units. Therefore, unit mass times unit
acceleration should equal unit force. This gives a relation among these three units.
Because of such physical relations, all the mechanical units can be derived from the
units for three fundamental quantities. The three quantities ordinarily taken as funda-
mental are mass, length, and time. Thermal quantities are conveniently derived from
these three quantities together with another fundamental quantity, temperature. Photo-
metric quantities are derived from the three fundamental mechanical quantities together
with luminous intensity as a fourth fundamental quantity.
Similarly, electrical and magnetic quantities are derived from the three fundamental
mechanical quantities and one fundamental electrical or magnetic quantity.
Two systems of mechanical units are in use in English-speaking countries, the English
and the metric systems. The metric system is used universally by physicists and to a
great extent by engineers, although the English system is still very common in engineering.
The English system uses the foot, the pound, and the second as the units for length, mass,
and time, respectively. The metric system (as used in the current literature — see MKS
system below) employs the meter, the kilogram, and the second as the units for length,
mass, and time, respectively.
STANDARDS OF THE FUNDAMENTAL UNITS. The physical units upon which
these fundamental units are based and the legalized standards of the United States and
Great Britain are described below.
Standard of Length. The standard meter (100 cm) is the distance between two lines
on a platinum-iridium bar carefully preserved at the Bureau of Weights and Measures,
at Sevres, France, when the bar is kept at a uniform temperature of 0 deg cent throughout.
In the United States the yard (3 ft) was defined by Act of Congress, July 28, 1866, as
1 U. S. yard = 7 meter
and similarly the British imperial yard is defined by law as
1 British imperial yard « 3Qg7 Q7Q meter
For engineering purposes the U. S. and British yards may be considered identical.
Standard of Mass and Force. The standard kilogram (1000 grams) is the mass of
a cylinder of platinum preserved at the Bureau of Weights and Measures, at Sevres
France. The U. S. pound avoirdupois is defined by law (Act of Congress, 1866) as
2.2046 kg' but k 1S93' the SuPerinten<knt of Weights and Measures, with the approval of
the Secretary of the Treasury, declared the pound to be
1U'S-lb = 2
The British imperial pound has the same value.
The same relations between the pound and kilogram hold whether these units be taken
as units of mass or as units of force, the unit of force being defined in both cases as the pull
of the earth on unit mass at 45 deg latitude and sea level
SYSTEMS OF UNITS 1-43
Standard of Time. The standard second universally adopted is the -zrr-:-:^ part of a
mean solar day. The solar day is the interval of time between two successive transits of
the sun across a meridian of the earth at the point of observation; this interval varies
in length at different times during the year, but the average length of the interval for one
year is constant as far as can be determined by any known methods of observation.
Temperature Scales. Two units of temperature, or temperature scales, are commonly
employed, viz., the centigrade and the fahrenheit units. The relation between these two
units results solely from the manner in which they are denned. One degree centigrade
= % degree fahrenheit. Owing to the difference in the zeros of the two scales, a tem-
perature of tf degrees fahrenheit corresponds to a temperature of tc = 5/9(£/ — 32) degrees
centigrade, and vice versa, t/ — 9/5 tc + 32 degrees fahrenheit.
Standard of Luminous Intensity. Before Jan. 1, 1948, the standard of luminous in-
tensity was the mean intensity in the horizontal plane from a group of incandescent lamps
maintained by the National Bureau of Standards (U. S.), in cooperation with similar
custodians in France, Great Britain, and Germany. The International candle was a point
source of light having an intensity of a definite fraction of this standard intensity.
The National Bureau of Standards, in pursuance of decisions of the International Com-
mittee on Weights and Measures, decided that, beginning Jan. 1, 1948, it would take as
the primary standard for the system of photometric units a black-body radiator operated
at the temperature of freezing platinum. The "candle," unit of intensity, is denned as
one-sixtieth of the intensity of one square centimeter of such a radiator. Other units are
derived from the candle, with the provision that when differences of color are involved the
evaluation shall be made by means of standard spectral luminosity factors which have been
adopted by the International Commission on Illumination and the International Com-
mittee on Weights and Measures.
ELECTRIC UNITS. Three systems of electric and magnetic units are in general use,
viz., (1) the cgs electrostatic system, (2) the cgs electromagnetic system, and (3) the
practical system. In the cgs electrostatic system the dielectric coefficient, «, of air * at
0 deg cent and 760 mm mercury pressure is arbitrarily chosen as unity. In the cgs elec-
tromagnetic system the magnetic permeability of air under the same standard conditions
is arbitrarily chosen as unity. In the practical system a concrete standard of the unit of
resistance (called the ohm) and of the unit of current (ampere) is arbitrarily chosen
(it was stated above that only one electric or magnetic unit need be chosen; the choice of
two leads to inconsistencies; see below) ; the unit of resistance is closely equal to 109 times
the unit of resistance in the cgs electromagnetic system and the unit current is approxi-
mately 0.1 that in the latter system. Occasionally other (special) systems are used, most
of which are designed to get rid of a factor 4?r which frequently appears in the usual
systems. The most popular of these others is the Heaviside— Lorentz system in which
the unit of electric charge is I/V^TT of the unit in the electrostatic system. (See MKS
system.)
Use of the Prefixes "Stat" and "Ab." To designate the electric and magnetic units
in the electrostatic and electromagnetic systems of units respectively, the prefixes "stat"
and "ab" may be used with the name of the corresponding practical unit. For example,
the cgs electrostatic unit of electric charge may be called the statcoulomb and the cgs
electromagnetic unit of electric charge may be called the abcoulomb, etc. f
Relations among the Three Systems of Electrical Units. The fundamental relations,
experimentally determined, between the cgs electrostatic and the cgs electromagnetic
system is that 1 abfarad — 8.9878 X 1020 statfarads, which may be approximated for
engineering purposes to
1 abfarad = 9 X 1020 statfarads
which, as a consequence of the definition of the various terms, is equivalent to
1 abcoulomb = 3 X 1010 stat coulombs
the erg being the unit of energy in both systems. Rigorously,
1 abcoulomb - 2.9979 X 1010 statcoulombs
(See the article by Birge, Rev. of Mod. Pkys., Vol. 1, 1 [July 1929].)
* Rigorously, eo of free or empty space is chosen unity; for air at 0 deg cent and 76 cm mercury
pressure <=o = 1.000585; see International Critical Tables, Vol. 6, 77, for the value of « for air under
various conditions.
t This abcoulomb, the unit of quantity of electricity in the electromagnetic system, should not be
confused with an "absolute coulomb," which is a unit closely equal to the coulomb and is what the
latter would be if 1 international or practical ohm equaled exactly 109 abohms and 1 ampere equaled
exactly 0.1 abamp. For engineering purposes, the difference between an absolute coulomb and a
coulomb is negligible.
1_44 MATHEMATICS, UNITS, AND SYMBOLS
The fundamental relations between the cgs electromagnetic system and the practical
system are
1 abcoulomb =10 coulombs
1 erg = 10 ~7 watt-second or joule
the erg being the unit of energy in the cgs electromagnetic system and the joule (or watt-
second) that in the practical system.
Practical Electrical Units. The former (see below) legal units of electrical measure in
the United States are given in an Act of Congress, July 12, 1894. Unfortunately, the
units there defined are not consistent with one another; for example, the unit of power
(watt) there given is not equal to the unit of power derived from the units of current
(ampere) and voltage (volt) as defined in the Act. The practical units (the so-called
international units) in use before Jan. 1, 1948, are based on the following two definitions:
The unit of resistance is the (international) ohm and is equal to the resistance offered
to an unvarying electric current by a column of mercury at the temperature of melting ice,
14.4521 grams in mass, of a constant cross-sectional area and 106.300 cm in length.
The unit of current is the (international) ampere and is equal to the unvarying electric
current which, when passed through a solution of nitrate of silver in accordance with
certain specifications, deposits silver at the rate of 0.00111800 gram per second.
The unit of electromotive force, the (international) volt, is derived from the above by
Ohm's law. Other international units are derived from these.
The National Bureau of Standards, in agreement with decisions of the International
Committee on Weights and Measures, decided to use as standard, beginning Jan. 1, 1948,
the electrical units "derived from the fundamental mechanical units of length, mass, and
time by use of accepted principles of electromagnetism, with the value of the permeability
of space taken as unity in the eentimeter-gram-second system or as 10 ~7 in the correspond-
ing meter-kilogram-second system." The reference is to the unrationalized MKS sys-
tem; in the rationalized MKS system, the permeability of space is 4n- X 10~7 henry per
meter.
In explanation of the legal status of the new standard, the Bureau states, "When the
electrical units were defined by law (Public Law No. 105, 53rd Congress) in 1894 it was
supposed that the international units were practically identical with the corresponding
multiples of the centimeter-gram-second electromagnetic system. Alternative definitions
were given for most of the units, and those definitions which appear to be legally control-
ling were taken partly from one system and partly from the other. The joule and the
watt, for example, are clearly denned as multiples of the cgs units. In brief, the absolute
units have as good a legal basis under the terms of that act as do the present international
units. New legislation is being proposed to remove the ambiguities of the old act, but
there should be no objection on legal grounds to the general adoption of the absolute units
even in advance of Congressional action."
Using "international" to refer to the previous standard, and "absolute" to refer to the
new, the relations accepted by the International Committee on Weights and Measures at
its meeting in Paris in October, 1946, are as follows:
1 mean international ohm = 1.00049 absolute ohms
1 mean international volt = 1.00034 absolute volts
The mean international units to which the above equations refer are the averages of
units as maintained in the national laboratories of the six countries (France, Germany,
Great Britain, Japan, U.S.S.R., and the United States) which took part in this work be-
fore the war. The units maintained by the National Bureau of Standards differ from
these average units by a few parts in a million, so that the conversion factors for adjusting
values of standards in this country will be as follows :
1 international ohm (U. S.) = 1.000495 absolute ohms
1 international volt (U. S.) = 1.00033 absolute volts.
Other electrical units will be changed by amounts shown in the following table:
1 international ampere = 0.999835 absolute ampere
1 international coulomb « 0.999835 absolute coulomb
1 international henry = 1.000495 absolute henrys
1 international farad = 0.999505 absolute farad
1 international watt = 1.000165 absolute watts
1 international joule = 1.000165 absolute joules
SYSTEMS OF UNITS * 1-45
The Act of 1894 defined the international ohm as previously stated, but denned the ampere
as 0.1 abampere. These units give rise to the so-called "semiabsolute" system, which is
seldom used.
THE MKS SYSTEM OF UNITS. In 1904 Giorgi proposed a system of units in which
the fundamental units were the meter, the kilogram, the second, and the ohm. Using
this system of fundamental units, the permeability of free space is MO = 4?r X 10~7 henry
per meter, and the equations of electricity and magnetism, using the practical units,
become equations without factors such as 108, etc. Such a system is similar to the so-
called absolute systems such as the cgs electromagnetic and the cgs electrostatic systems.
It follows from the theory of radiation of electromagnetic waves that the dielectric coeffi-
cient <=o = — ; , where c is the ratio of electromagnetic to electrostatic units, which can be
Moc2
taken as the velocity of light in free space.
The International Committee of Weights and Measures, at its meeting in October 1946,
decided that the actual substitution of this absolute system of electrical units for the inter-
national system should take place on January 1, 1948.
The units are then defined by a set of definitions such as follows:
(a) Ampere. The ampere is the constant current which, maintained in two parallel
rectilinear conductors of infinite length separated by a distance of 1 meter, produces
between these conductors a force equal to 2 X 10 ~7 mks (meter-kilogram-second) units
of force per meter of length.
(b) Volt. The volt is the difference of electrical potential between two points of a
conductor carrying a constant current of 1 ampere when the power dissipated between
these points is equal to 1 mks unit of power (watt).
(c) Coulomb. The coulomb is the quantity of electricity transported each second by
a current of 1 ampere.
(d) Ohm. The ohm is the electrical resistance between two points of a conductor
when a constant difference of potential of 1 volt, applied between these points, produces
in the conductor a current of 1 ampere, the conductor not being the seat of an electro-
motive force.
(e) Weber. The weber is the magnetic flux which, traversing a circuit of a single
turn, would produce an electromotive force of 1 volt, if brought to zero in 1 second with
uniform diminution.
(f) Henry. The henry is the inductance of a closed circuit in which an electromotive
force of 1 volt is produced when the electric current traversing the circuit varies uni-
formly at the rate of 1 ampere per second.
(g) Farad. The farad is the electrical capacitance of a capacitor between the plates
of which appears an electrical difference of potential of 1 volt, when charged with 1 coulomb
of electric charge.
The original Giorgi MKS system chose the ohm as the fourth fundamental unit. This
choice has not been confirmed. The electrical fundamental unit could be almost any of
the electrical units. No particular unit has as yet been chosen as fundamental. The
preferences seem to be divided between the ampere, the ohm, the permeability, and the
coulomb.
The original Giorgi MKS system chose fj-o = 4-7rlO~7 henry per meter, the 4?r factor caus-
ing the electromagnetic formulas expressing rectilinear symmetry, such as the Maxwell
equations, to be free of the factor 4?r, and the electromagnetic formulas expressing circular
symmetry, such as Coulomb's law, to contain the factor 47r. Such a system is called a
rationalized system as contrasted with a non-rationalized system, examples of which are
the electromagnetic and the electrostatic cgs systems. The non-rationalized MKS system
corresponding to the original Giorgi system is defined by the choice of JUQ ~ 10~7. This
changes the values of some of the units as shown in the table below.
1-46
MATHEMATICS, UNITS, AND SYMBOLS
Rationalized MKS Units and Corresponding COS Electromagnetic Units
Multiply mks units by F to obtain cgs units
Quantity
Symbol
MKS Unit
CGS Unit
F
Mechanical
JjQQOrtil
L
m
cm
10;*
M
kg
g
103
Time
T
sec
sec
.L
.Area »
s
sq m
sq cm
10*
V
cu m (stere)
cu cm
106
f
cycle per sec (hertz)
cycle per sec
1
Density
d
kg per cu m
g per cu cm
10 3
Velocity
V
m per sec
cm per sec
10*
a
m per sec per sec
cm per sec per sec
10*
Force
F
newton (j per m).
dyne
106
Pressure
P
newton per sq m
dyne per sq cm
10
*,0
radian
radian
1
.Angular velocity . .
w
radian per sec
radian per sec
1
T
j per radian
dyne cm
10I
^loment of inertia
J
kg-sq m
g-sq cm
107
Energetics
"Work or eneroy . ...
w
j
erg
107
Volume energy or energy
density .
w
j pei* cu m
erg per cu cm
10_
Active power
P
w
erg per sec
107
Reactive power
Q
var
erg per sec
107
Thermal
Quantity of heat
Q
kg cal
g cal
103
Temperature
e
C or K
C or K
1
Luminous
Intensity . .
I
candle
candle
1
t
1
1
1 A
IlTuminatipn ... ......
E
lux
phot
lo-J
Brightness
b
C8.nrJl6 p<»f gq rn
stilb
10~4
Elec'rical
Electromotive force . . .
E
volt
abvolt
108
Potential gradient or elec-
tric field, intensity
E
volt ppr m
abvolt per cm
106
Resistance
R
ohm
abohm
109
Resistivity
p
ohm-m
ab ohm-cm
1011
Conductance
G
siemens mho
abmho
10~9
Conductivity
y
mho per m
abmho per cm
lo-11
§uantity or displacement . .
urrent
}
coulomb
amp
abcoulomb
abamp
10-1
10-1
Electric flux ....
•%
coulomb
abcoulomb
10~1
Flux density
D
coulomb per sq m
abcoulomb per sq cm
o-6
Current density
i
ampere per sq m
abampere per sq cm
io-B
Capacitance
c
farad
abfarad
10"~9
Specific inductive capacity.
Dielectric coefficient for
free space or space ca-
pacitivity
e/eo
£Q
numeric
107/47rc2 — 8 854 X 10~12
numeric
4 = 1.113 X NT21
1
Magnetic
Magnetomotive force
$
ftTnp-tlTm
gilbert
4?r 1 0""1
Magnetizing force or mag-
netic field intensity
Space permeability
H
MO
amp-turn per m
47r]0-7 - ] 257 x 10~6
oersted
1
47T 1 0~3
Relative permeability
Magnetic flux
M/MO
4>
numeric
Weber
numeric
108
Flux density
B
ir)4
Reluctance
(R
amp-turn per weber
gauss
4T j Q^S
Permeance
(P
i n9 //!_..
Inductance
L
h ^ ^
, ,
1 fi9
Pole strength
in
weber
aonenry
108 /4_.
Magnetization
cr
e i/ TT
i n4 /A
Magnetic moment
m
weber-m
maxwell-cm/Mr
1010/4*
Rationalized MKS Units and Corresponding Non-rationalized Units
Multiply non-rationalized mks units by F to obtain rationalized mks units
Quantity
Symbol
Name of Rationalized MKS Units
F
Electrical
Electric flux
¥
D
€0
M or 5
H
fJ-O
(P
(R
m
m
B
coulomb
coulomb per sq m
farad per m
amp-turn
amp-turn per m
henry per m
weber per amp-turn
amp-turn per weber
weber
weber-m
weber per sq m
4*
4ir
47T
1/47T
r
47T
l/4,r
47T
4T
47T
Flux density . .
Space capacitivity
Magnetic
Magnetomotive force
Magnetizing force
Space permeability . .
Permeance
Reluctance
Pole strength
Magnetic moment
Flux density
CONVERSION TABLES
1-47
17. CONVERSION TABLES
Table 1. Length [L]
Multiply
N. Number
\Kof~*
N^X
to XSN
Obtain \>C
± N
1
•g
1
J
Kilometers
Nautical miles
1
,
s
Millimeters 1
£
Centimeters
1
30.48
2.540
105
1.853
X105
100
2.540
X10-3
1.609
X105
0.1
91.44
Feet
3.281
XI 0-2
I
8.333
XI 0-2
3281
6080.27
3.281
8.333
X10-5
5280
3.281
X10-3
3
Inches
0.3937
12
1
3.937
XIO*
7.296
XIO*
39.37
0.001
6.336
X10*
3.937
XI 0-2
36
Kilometers
10-6
3.048
X10-4
2.540
X10-6
1
1.853
0.001
2.540
X10-8
1.609
10-6
9.144
X1CM
Nautical miles
1.645
XI 0-4
0.5396
1
5.396
X10-4
0.8684
4.934
xio-<
Meters
0.01
0.3048
2.540
XI 0-2
1000
1853
1
1609
0.001
0.9144
Mils
393.7
1.2
X104
1000
3.937
xio?
3.937
X104
1
39.37
3.6
X104
Miles
6.214
XlO-e
1,894
XI 0-4
1.578
X10-5
0.6214
1.1516
6.214
XI O-*
1
6.214
X10-7
5.682
X10-4
Millimeters
10
304.8
25.40
106
1000
2.540
XI 0-2
1
914.4
Yards
1.094
XI 0-2
0.3333
2.778
XI 0-2
1094
2027
1.094
2.778
X10-5
1760
1.094
X10-3
1
Metric Multiples
10fl microns — 103 millimeters = 102 centimeters = 10 decimeters = 1 meter
= 10"1 dekameter — 10~2 hectometer « 10~3 kilometer = 10~4 myriameter
= 10~8 megameter = 1010 Angstrom Units.
Land Measure
7.92 inches = 1 link
25 links = 1 rod = 16.5 feet — 5.5 yards (1 rod = 1 pole = 1 perch)
4 rods = 1 chain (Gunther's) = 66 feet = 22 yards = 100 links
10 chains = 1 furlong = 660 feet = 220 yards = 1000 links = 40 rods
8 furlongs = 1 mile = 5280 feet = 1760 yards = 8000 links = 320 rods = 80 chains
Ropes and Cables
2 yards = 1 fathom 120 fathoms = 1 cable's length
Nautical Measure
6080.27 feet = 1 knot « 1 nautical mile — 1.15156 statute miles *
3 nautical miles = 1 league (U. S.) 3 statute miles = 1 league (Gr. Britain)
(NOTE. — A knot, or nautical mile, is the length of a minute of longitude of the earth
at the equator at sea level. The British Admiralty uses the round figure of 6080 feet.
The word "knot" is frequently used also to denote "nautical miles per hour.")
Miscellaneous
3 inches = 1 palm
4 inches = 1 hand
9 inches
2 1/2 feet -.
• 1 span
: 1 military pace
1-48 MATHEMATICS, UNITS, AND SYMBOLS
Table 2. Area |Z2J
Multiply
Nv Number
Obtain N!^
g
o
]
1
1
§
i
I
8
I
02
Square kilometers
|
Square miles
1
tu
1
Square yards
Acres
1
2.296
XI 0-5
247.1
2 471
X10-1
640
2.066
XIO-4
Circular mils
1
1.973
X10&
1.833
XI08
1.273
X10G
1.973
1973
Square centimeters
5.067
XI 0-e
1
929.0
6.452
lOio
104
2.590
XI 0*0
0.01
8361
Square feet
4.356
1.076
X10-3
1
6.944
XI 0-3
1.076
XIO?
10.76
2.788
X107
1.076
xio-*
9
Square inches
6,272,640
7.854
XI 0-7
0.1550
144
1
1.550
1550
4.015
X109
1.550
X10-3
1296
Square kilometers
4.047
X10-3
10-10
9.290
X10-8
6.452
XI O-io
1
10-8
2.590
10-12
8.361
X10-7
Square meters
4047
0.0001
9.290
XI 0-2
6.452
XIO-4
100
1
2.590
X10C
10-o
0.8361
Square miles
1.562
XI 0-3
3.861
XI O-ii
3.587
XI 0-8
0.3861
3 861
XI 0-7
1
3.861
XI 0-13
3.228
XIO-7
Square millimeters
5.067
XI 0-4
100
9.290
XIO*
645.2
1012
106
1
8.361
X105
Square yards
4840
1.196
XIO-4
0.1II1
7.716
XIO-4
1.196
X106
1.196
3,098
1,196
X10-6
1
Land Measure
30 1/4 square yards = 1 square rod = 272 1/4 square feet
16 square rods = 1 square chain = 484 square yards = 4356 square feet
2 1/2 square chains = 1 rood = 40 square rods = 1210 square yards
4 roods = 1 acre = 10 square chains =160 square rods
640 acres = 1 square mile = 2560 roods = 102,400 square rods
1 section of land = 1 square mile; 1 quarter section =160 acres
Architect's Measure
100 square feet = 1 square
Circular Inch and Circular Mil
A circular inch is the area of a circle 1 inch in diameter = 0.7854 square inch
1 square inch = 1.2732 circular inches
A circular mil is the area of a circle 1 mil (or 0.001 inch) in diameter = 0.7854 square mil
1 square mil = 1.2732 circular mils
1 circular inch = 105 circular mils = 0.7854 X 106 square mils
1 square inch = 1.2732 X 105 circular mils = 106 square mils
Metric Multiples
1 square meter = 1 centiare = 10~2 are = 10™4 hectare
— 10~~6 square kilometer = 10~8 square myriameter
CONVERSION TABLES
1-49
Table 3. Volume [I8]
Multiply
\. Numfrfif
E
'^^
I
•8
I
J
2
-§^
Q S
1
1
B
?2
1
Obtain ^VN
^ ^
«
I
o
I
1
o
.2 J
I-3
o
1
§
1
-2
I
Bushels (dry)
1
0.8036
4.651
28.38
2.838
xio-4
XIO-2
Cubic centimeters
3.524
1
2.832
16.39
106
7.646
3785
1000
473.2
946.4
XIO*
XIO*
xio5
Cubic feet
1 .2445
3.531
1
5.787
35.31
27
0.1337
3.531
1.671
3.342
X10-5
X10-4
XIO-2
xio-s
XIO-2
Cubic bches
2150.4
6.102
1728
1
6.102
46,656
231
61.02
28.87
57.75
XIO-2
XltK
Cubic meters
3.524
10-6
2.832
1.639
1
0.7646
3.785
0.001
4.732
9.464
(steres)
XIO-2
XIO-2
XI 0-5
X10-3
xio-*4
XIO-*
Cubic yards
1.308
3.704
2.143
1.308
1
4.951
1.308
6.189
1.238
XlO-e
XIO-2
X10-5
XI 0-3
X10-3
X10-4
XlO-s
Gallons (liquid)
2.642
7.481
4.329
264.2
202.0
1
0.2642
0.125
0.25
X10-4
X10-3
Liters
35.24
0.001
28.32
1.639
1000
764.6
3.785
1
0.4732
0.9464
XIO-2
Pints (liquid)
2.113
59.84
3.463
2113
1616
8
2,113
1
2
XI 0-3
xio-^
t
Quarts (liquid)
1.057
29.92
1.732
1057
807.9
4
1.057
0.5
1
XI 0-3
XIO-2
Acre-feet: multiply number of acre-feet by 4.356 X 104 to obtain number of cubic feet;
multiply by 3.259 X 105 to obtain number of gallons.
Metric Multiples
10 milliliters = 1 centiliter = 0.338 fluid ounce
10 centiliters = 1 deciliter = 0.845 liquid gill
10 deciliters = 1 liter = 1.0567 liquid quarts
10 liters = 1 dekaliter — 2.6417 liquid gallons
10 dekaliters = 1 hectoliter = 2.8375 U. S. bushels
10 hectoliters = 1 kiloliter (or stere) = 28.375 U. S. bushels
Cubic Measure
1 cord of wood = a pile cut 4 feet long, piled 4 feet high and 8 feet on the
ground — 128 cubic feet
1 perch of stone = a quantity 1 1/2 feet thick, 1 foot high and 16 !/2 feet long
= 24 3/4 cubic feet
(NOTE. — A perch of stone is, however, often computed differently in different locali-
ties; thus, in most if not all of the States and Territories west of the Mississippi, stone-
masons figure rubble by the perch of 16 1/2 cubic feet. In Philadelphia, 22 cubic feet are
called a perch. In Chicago, stone is measured by the cord of 100 cubic feet. Check
should be made against local practice.)
Board Measure
In board measure, boards are assumed to be one inch in thickness. Therefore, feet
board measure of a stick of square timber = length in feet X breadth in feet X thickness
in inches.
1-50 MATHEMATICS; UNITS, AND SYMBOLS
Shipping Measure
For register tonnage or measurement of the entire internal capacity of a vessel, it is
arbitrarily assumed, to facilitate computation, that:
100 cubic feet = 1 register ton
For the measurement of cargo:
40 cubic feet = 1 U. S. shipping ton = 32.143 U. S. bushels
42 cubic feet = 1 British shipping ton = 32.703 Imperial bushels
Dry Measure
One IT. S. Winchester bushel contains 1.2445 cubic feet or 2150.42 cubic inches. It
holds 77.601 pounds distilled water at 62 deg fahr.
(NOTE. — The above is a struck bushel. A heaped bushel in general equals 1 !/4 struck
bushels, although for apples and pears it contains 1.2731 struck bushels = 2737.72 cubic
inches.)
One U. S. gallon (dry measure) = Vs bushel and contains 268.8 cubic inches.
(NOTE. — This is not a legal IT. S. dry measure and therefore is given for comparison
only.)
One British Imperial bushel contains 1.2843 cubic feet or 2219.36 cubic inches. It holds
80 pounds distilled water at 62 dog fahr.
One British Imperial gallon = 1/8 Imperial bushel and contains 277.42 cubic inches.
1 Winchester bushel = 0.9694 Imperial bushel
1 Imperial bushel =* 1.032 Winchester bushels
Same relations as above maintain for gallons (dry measure)
[NOTE.— 1 U. S. gallon (dry) = 1.164 U. S. gallons (liquid).]
U. S. Units
2 pints = 1 quart = 67.2 cubic inches
4 quarts = 1 gallon * = 8 pints = 268.8 cubic inches
2 gallons * = 1 peck = 16 pints = 8 quarts — 537.6 cubic inches
4 pecks = 1 bushel = 64 pints = 32 quarts = 8 gallons * = 2150.42 cubic inches
1 cubic foot contains 6.428 gallons (dry measure) *
Liquid Measure
One U. S- gallon (liquid measure) contains 231 cubic inches. It holds 8.336 pounds
distilled water at 62 deg fahr.
One British Imperial gallon contains 277.42 cubic inches. It holds 10 pounds distilled
water at 62 deg fahr.
1 U. S. gallon (liquid) = 0.8327 Imperial gallon
1 Imperial gallon = 1.201 U. S. gallons (liquid)
[NOTE.— 1 U. S. gallon (liquid) = 0.8594 U. S. gallon (dry).]
U. S. Units
4 gills = 1 pint = 16 fluid ounces
2 pints = 1 quart = 8 gills - 32 fluid ounces
4 quarts = 1 gallon = 32 gills = 8 pints =128 fluid ounces
1 cubic foot contains 7.4805 gallons (liquid measure)
Apothecaries' Fluid Measure
60 minims = 1 fluid drachm. 8 drachms = 1 fluid ounce
In the TJ. S. a fluid ounce is the 128th part of a U. S. gallon, or 1.805 cu in. or
29.58 cu cm. It contains 455.8 grains of water at 62 deg fahr. In Great Britain the fluid
ounce is 1.732 cu in. and contains 1 ounce avoirdupois (or 437.5 grains) of water at 62 deg
fahr.
* The gallon is not a U. S. legal dry measure.
Table 4. Plane Angle [No Dimensions]
Multiply
Number
^N. of-^
Revolu-
t\>N^
Degrees
Minutes
Quadrants
Radians *
(Circum-
Seconds
Obtain ^sX*
ferences)
4- ^
Degrees
1
K667
90
57.30
360
2.778
XI 0-2
XlO-4
Minutes
60
1
5400
3438
2.16
1.667
xio*
X10-2
Quadrants
Kill
K852
1
0.6366
4
3.087
X10-2
XlO-4
X10-6
Radians *
K745
2.909
1.571
1
6.283
4.848
XI 0-2
XlO-4
XlO-c
Revolutions *
2.778
4.630
0.25
0, 1591
1
7.716
(Circumferences)
XIO-3
X10-5
X10-7
Seconds
3600
60
3.24X105
2.063X105
1.296X106
1
* 27T radians = 1 circumference — 360 degrees by definition.
Table 5. Solid Angle [No Dimensions]
Multiply
Number
of-»
Hemispheres
Sphe:
Spherical
right angles
Steradians t
Hemispheres
0.25
0. 1592
Spheres *
0.5
0.125
7.958 X 10-2
Spherical right angles
0.6366
Steradians f
6.283
12.57
1.571
* A sphere is the total solid angle about a point. Lf 4ir Steradians = 1 sphere by definition.
Table 6. Time [T]
Multiply
X Number
of— ^
.^
Obtain \X^
Days
Hours
Minutes
Months
(average) *
Seconds
Weeks
Days
1
4.167
XI 0-2
6.944
30.42
1.157
XI 0-5
7
Hours
24
1
1.667
XI 0-2
730.0
2.778
168
Minutes
1440
60
1
4.380
1.667
X10-2
K008
X104
Months (average) *
3.288
XI 0-2
1.370
XIO-3
2.283
XI 0-5
1
3.806
X10-7
0.2302
Seconds
8.64
X104
3600
60
2.628
X106
1
6.048
X105
Weeks
0. 1429
5.952
XI 0-3
9.921
XI 0-5
4.344
K654
XI 0-6
1
* One common year = 365 days; one leap year = 366 days; one average month = Ms of a
common year.
1-51
1-52 MATHEMATICS, UNITS, AND SYMBOLS
Table 7. Linear Velocity [LT~l]
v Multiply
v >v Number
'"X^v
Obtain \N>
4, V\<
S"d
ii
o
Feet per minute
1
1
i
03 9
| fe
1
|
Meters per second
1
1
I
Centimeters
per second
1
0.5080
30.48
27.78
1667
51.48
1.667
100
44.70
2682
Feet per minute
1.969
1
60
54.68
3281
101.3
3.281
196.8
88
5280
Feet per second
3.281
1.667
XIO-2
1
0.9113
54.68
1.689
5.468
XIO-2
3.281
1.467
88
Kilometers per hour
0.036
1.829
XIO-2
1.097
1
60
1.853
0.06
3.6
1.609
96.54
Kilometers
per minute
0.0006
3.048
xio-*
1.829
XIO-2
1.667
XIO-2
1
3.088
XIO-2
0.001
0.06
2.682
XIO-2
1.609
Knots*
1.943
XIO-2
9.868
XI 0-3
0.5921
0.5396
32.38
1
3.238
XlO-a
1.943
0.8684
52.10
Meters per minute
0.6
0.3048
18.29
16.67
1000
30.88
1
60
26.82
1609
Meters per second
0.01
5.080
XI 0-3
0.3048
0.2778
16.67
0.5148
1.667
1
0.4470
26.82
Miles per hour
2.237
XIO-2
1.136
XIO-2
0.6818
0.6214
37.28
1.152
3.728
XIO-2
2.237
1
60
Miles per minute
3.728
X10-4
1.892
1.136
XIO-2
1.036
X10-a
0.6214
1.919
XIO-2
6.214
3.728
XIO-2
1.667
XIO-2
1
* Nautical miles per hour.
The Miner's Inch
(Used in Measuring Flow of Water)
An Act of the California legislature, May 23, 1901, makes the standard miner's inch
1.5 cu ft per minute, measured through any aperture or orifice.
The term miner's inch is more or less indefinite, for the reason that California water
companies do not all use the same head above the center of the aperture, arid the inch
varies from 1.36 to 1.73 cu ft per minute, but the most common measurement is through
an aperture 2 in. high and whatever length is required, and through a plank 1 1/4 in. thick.
The lower edge of the aperture should be 2 in. above the bottom of the measuring-box,
and the plank 5 in. high above the aperture, thus making a 6-in. head above the center
of the stream. Each square inch of this opening represents a miner's inch, which is equal
.to a flow of 1.5 cu ft per minute.
CONVERSION TABLES
1-53
Table 8. Angular Velocity [T*1]
Multiply
Number
of-*
Degrees
per second
Radians
per second
Revolutions
per minute
Revolutions
per second
Degrees per second
57.30
360
Radians per second
1.745X10-2
0.1047
6.283
Revolutions per minute
0.1667
9.549
60
Revolutions per second
2.778X10-3 0.1592
. 667 X IP"2
Table 9. Linear Acceleration * [LT~2]
Multiply
-x. Number
X\. of->
t>^x.
Obtain ^xN^
•^ >^
Centimeters
per second
per second
Feet
per second
per second
Kilometers
per hour
per second
Meters
per second
per second
Miles
per hour
per second
Centimeters per second
per second
1
30.48
27.78
100
44.70
Feet per second per
second
3.281 X 10-2
1
0.9113
3.281
1.467
Kilometers per hour
per second
0.036
1.097
i
3.6
1.609
Meters per second per
second
0.01
0.3048
0.2778
1
0.4770
Miles per hour per
second
2.237 X 10-2
0.6818
0.6214
2.237
,
* The (standard) acceleration due to gravity (#0) = 980.7 cm per sec per sec = 32.17 feet
per sec per sec = 35.30 km per hour per sec = 9.807 meters per sec per sec = 21.94 miles per hour
per sec.
Table 10. Angular Acceleration [T~'2]
Multiply
Number
of->
Radians
per second
per second
Revolutions
per minute
per minute
Revolutions
per minute
per second
Revolutions
per second
per se§ond
Radians per second per second
.745X10-3
0. 1047
6.283
Revolutions per minute per minute
573.0
1
60
3600
Revolutions per minute per second
9.549
1.667X10-2
60
Revolutions per second per second
0.1592
2.778X10-
1.667X10-2
1-54
MATHEMATICS, UNITS, AND SYMBOLS
Table 11. Mass [M] and Weight *
Multiply
N. Number
to ^\Vv
Obtain \^v
1
O
1
i
!
H—
o
j
I
1
Tons (short)
Grains
1
15.43
1.543
xio4
1.543
437.5
7000
9.072
105
Grams
6.481
XIO'2
1
1000
0.001
28.35
453.6
1.016
106
Kilograms
6.481
XlO-s
0.001
1
10-6
2 835
X10-2
0 4536
1016
1000
907.2
Milligrams
64.81
1000
106
1
2.835
4.536
X105
1.016
X109
109
9 072
X1Q8
Ounces f
2.286
3.527
35.27
3.527
X10-5
1
16
3.584
3.527
3.2
xio4
Pounds t
1.429
2.205
XlO-3
2.205
2.205
X10-6
6.250
XIO-2
1
2240
2205
2000
Tons (long)
9.842
9\842
XI 0-4
9.842
XI O-io
2.790
4.464
1
0.9842
0.8929
Tons (metric)
10^5
0.001
10-9
2.835
XI 0-5
4 536
1.016
1
0.9072
Tons (short)
1.102
X10-6
-1.102
XlO-3
1 102
XI 0"9
3.125
XI 0-s
0.0005
1.120
1.102
1
* These same conversion factors apply to the gravitational units of force having the corresponding
names. The dimensions of these units when used as gravitational units of force are MLT~*; see
table for Force.
f Avoirdupois pounds and ounces.
Metric Multiples
106 micrograms = 103 milligrams = 102 centigrams
10"1 dekagram
gram
10 ~2 hectogram = 10 3 kilogram ;
10 decigrams
10"4 myriagram =•
= 1 gram =
10~8 mega-
Avoirdupois Weight
(Used Commercially)
27.343 grains = 1 drachm
16 drachms = 1 ounce (oz) = 437.5 grains
16 ounces = 1 pound (Ib) = 7000 grains
28 pounds = 1 quarter (qr)
4 quarters — 1 hundredweight (cwt) = 112 pounds
20 hundredweight = 1 gross or long ton *
2000 pounds = 1 net or short ton
(* NOTE. — The long ton is used by the U. S. custom-houses in collecting duties upon
foreign goods. It is also used in freighting coal and selling it wholesale.)
14 pounds = 1 stone; 100 pounds = 1 quintal
Troy Weight
(Used in weighing gold or silver)
24 grains = 1 pennyweight (dwt)
20 pennyweights = 1 ounce (oz) = 480 grains
12 ounces = 1 pound (Ib) = 5760 grains
The grain is the same in Avoirdupois, Troy and Apothecaries' weights. A carat, for
weighing diamonds = 3.086 grains = 0.200 gram. (International Standard, 19.13.)
1 pound troy = .8229 pound avoirdupois
1 pound avoirdupois = 1.2153 pounds troy
CONVEKSION TABLES
1-55
Apothecaries' Weight
(Used in compounding medicines)
20 grains — 1 scruple O)
3 scruples = 1 drachm (3 ) — 60 grains
8 drachms = 1 ounce (§) = 480 grains
12 ounces = 1 pound (Ib) = 5760 grains
The grain is the same in Avoirdupois, Troy and Apothecaries' weights.
1 pound apothecaries = 0.82286 pound avoirdupois
1 pound avoirdupois = 1.2153 pounds apothecaries
Table 12. Density or Mass per Unit Volume [ML~3]
Grams per
cubic
centimeter
Kilograms
per
cubic meter
Pounds per
cubic foot
Pounds per
cubic inch
Grams per cubic centimeter
0.001
1 .602X 10-2
27.68
Kilograms per cubic meter
1000
16.02
2.768X104
Pounds per cubic foot
62.43
6.243X10-2
1728
Pounds per cubic inch
3.613X10-23.613X10-5
5.787X10-4
Pounds per mil foot *
3.405 X 10~7 3.405X 10 -1° 5.456X 10-9 9.425X1Q-6
* Unit of volume is a volume one foot long and one circular mil in cross-section area.
Table 13. Force * [MLT~2] or [F]
Multiply
s. Number
x\of-*
Obtain ^^"^^^
Dynes
Grams
Joules
per cm
Joules
per meter
(newtons)
Kilo-
grams
Pounds
Poundala
Dynes
1
980.7
107
105
9.807
X105
4.448
X105
1.383
X104
Grams
1.020
X\Q^S
1
1.020
XI 04
102.0
1000
453.6
14.10
Joules per cm
10-7
9.807
XI 0-5
1
.01
9.807
XI 0-2
4.448
XI 0-2
1.383
X10-3
Joules per meter
(newtons)
10-5
9.807
XlO-s
100
1
9.807
4.448
0. 1383
Kilograms
1.020
X\Q~*
0.001
10.20
0. 1020
1
0.4536
1.410
Pounds
2.248
x\o-&
2.205
XI 0-3
22.48
0.2248
2.205
1
3. 108
X10-2
Poundals
7.233
X10-5
7.093
X10-2
723.3
7.233
70.93
32.17
1
* Conversion factors between absolute
acceleration due to gravity conditions.
and gravitational units apply only under standard
1-56
MATHEMATICS, UNITS, AND SYMBOLS
Table 14. Torque or Moment of Force [MZ2T~2] or [FL] *
Multiply
X. Number
Obtain ^^OsX
Dyne-
centimeters
Gram-
centimeters
Kilogram-
meters
Pound-feet
Newton-
meter
Dyne-centimeters
1
980.7
9. 807 XIO7
1.356 XIO7
107
Gram-centimeters
1.020 XIO"3
1
105
1.383 XIO4
1.020 XIO4
Kilogram-meters
1.020 XIO"8
10"6
1
0.1383
0.1020
Pound-feet
7. 376 XIO"8
7.233X10"5
7,233
1
0.7376
Newton-meter
10"7
9.807X10~4
9.807
1.305
1
* Same dimensions as energy.
Table 15. Pressure or Force per Unit Area
x Multiply
n-§
i
>i
-w N. Number
*
§ a
§•43
S •«•
^0
1
£
t&i
£ JS
pd
«L
.-§
^X\
1
S o
11
•So
i0
S1!
Hi
|.a
5, o
f J
rd <t>
&8
Obtain ^VV
4- ^
1
I g
&a
m
a >»
1 %
§ °
P
r
i'
•s I
I1
P
P
II
&
Atmospheres *
1
9.869
xio-7
1.316
X10~2
3.342
xio~2
2.458
9.678
X10"5
4.725
XIO"4
6.804
XIO"2
0,9450
9.869
XIO"6
Baryes or dynes per
•1.013
1
1.333
3.386
2.491
98.07
478.8
6.895
9.576
10
square centimeter f
xio6
xio4
xio4
XIO"3
xio4
X 105
Centimeters of mer-
76.00
7.501
1
2.540
0.1868
7.356
3.591
5.171
71.83
7.501
cury at 0° C I
XIO"5
X10"3
X10"2
XIO"4
Inches of mercury at
29.92
2.953
0.3937
1
7.355
2.896
1.414
2.036
28.28
2.953
o°ct
xio~5
XIO 2
X10"3
xio 2
xio~4
Inches of water at
406.8
4.015
5.354
13.60
1
3.937
0.1922
27.68
384.5
4.015
4°C
X10"4
XIO 2
xio~3
Kilograms per square
1.033
1.020
136.0
345.3
25.40
1
4.882
703.1
9765
0. 1020
meter §
xio4
xio 2
Pounds per square
2117
2.089
27.85
70.73
5.204
0.2048
1
144
2000
2.089
foot
X10"3
X 10"2
Pounds per square
14.70
1.450
0.1934
0.4912
3.613
1.422
6.944
1
13,89
1,450
inch -
X10"5
xio~2
X10~3
XIO"3
XIO"4
Tons (short) per
1.058
1.044
1.392
3.536
2.601
1.024
0.0005
0.072
1
1.044
square foot
X10"6
X10"2
xio~2
X10"3
X10"4
XIO"6
Newtoos per square
1.013
10"1
1.333
3.386
2.491
9.807
47.88
6.895
9 576
1
meter
xio5
xio3
xio3
X10"4
X 103
XIO4
* Definition; One atmosphere (standard) = 76 cm of mercury at 0 deg cent,
f Sometimes caBed a bar.
t To convert height A of a column of mercury at i degrees Centigrade to the equivalent height A0 at 0 deg cent use
^ = h { l - ™+J } where m = 0.0001818 and I = 18.4 X 10"6 if the scale is engraved on brass; I - 8.5 X 10~6
luid) see International Critical Tables,
§ 1 gram per sq em = 10 kilograms per sq m.
CONVERSION TABLES
1-57
Table 16. Energy, Work and Heat * [ML^T^] or [FL]
Multiply
N. Number
Obtain ^"VV^
1
S3
1
Ergs or centimeter-
dynes
£
1
1
S 1
11
j1"!
j
j
I
British thermal
units t
1
9.297
XI 0-8
9.480
XI 0-n
1.285
XI 0-3
2545
9.480
3.969
3413
9.297
XI 0-3
3.413
Centimeter-grams
1.076
X107
1
1.020
XI 0-s
1.383
X1Q4
2.737
XI Oio
1.020
X104
4.269
X107
3.671
XI Oio
105
3.671
X107
Ergs or centimeter-
dynes
1.055
XI 01°
980.7
1
1.356
X107
2.684
XI 013
107
4.186
XI Oio
3.6
XI 013
9.807
X107
3.6
XI Oio
Foot-pounds
778.0
7.233
XI 0-6
7.367
X10-8
1
1.98
X106
0.7376
3087
2.655
X106
7.233
2655
Horsepower-hours
3.929
XI 0-4
3.654
x 10-11
3.722
5.050
X10-7
1
3.722
XI 0-7
1.559
XI 0-3
1.341
3.653
1.341
X10-3
Joules J or watt-
seconds
1054.8
9.807
10-7
1.356
2.684
X1Q5
1
4186
3.6
X106
9.807
3600
Kilogram-calories t
0.2520
2.343
X10-8
2.389
xi 0-11
3.239
XI 0-4
641.3
2.389
X10-4
1
860.0
2.343
XI 0-3
0.8600
Kilowatt-hours
2.930
XI 0-4
2.724
xi 0-11
2.778
XI 0-14
3.766
XI O-7
0.7457
2.778
XI 0-7
1.163
XI 0-3
1
2.724
'XI O-e
0.001
Meter-kilograms
107.6
10-s
1.020
XI 0-8
0.1383
2.737
X105
0.1020
426.9
3.671
I
367.1
Watt-hours
0.2930
2.724
XlO-a
2.778
xi 0-11
3.766
XI 0-4
745.7
2.778
X10-4
1.163
1000
2.724
XI 0-3
1
* See note at the bottom of Table 17.
t Mean calorie and Btu used throughout. One gram-calorie = 0.001 kilogram-calorie; one
Oatwald calorie = 0.01 kilogram-calorie.
The IT cal, 1000 international steam-table calories, has been denned as the 1 /860th part of the
international kilowatthour (see Mechanical Engineering, Nov., 1935, p. 710). Its value is very
nearly equal to the mean kilogram-calorie, 1 IT cal = 1.00037 ;kilogram-calories (mean). 1 .Btu =»
251.996 IT cal.
t Absolute joule, defined as 107 ergs. The international joule, baaed on the international ohm.
and ampere, equals 1,0003 absolute joules,
1-58 MATHEMATICS, UNITS; AND SYMBOLS
Multiply
^ >v Number
to \SsX
Obtain ^OO>
British thermal units
per minute
i
1
Foot-pounds per
second
w
W
Kilogram-calories
per minute
Kilowatts
Metric horsepower
1
British thermal units
per minute
1
5.689
X10-9
1.285
X10-3
7.712
XIO-2
42.41
3.969
56.89
41.83
5.689
XIO-2
Ergs per second
1.758
1
2.259
X1Q5
1.356
X107
7.457
X109
6.977
X108
1010
7.355
X109
107
Foot-pounds per
minute
778.0
4.426
X10-6
1
60
3.3
3087
4.426
xio*
3.255
44.26
Foot-pounds per
second
12.97
7.376
XI 0-8
1.667
XIO-2
1
550
51.44
737.6
542.5
0.7376
Horsepower *
2.357
XIO-2
1.341
3.030
X10-5
1.818
X10-3
1
9.355
XIO-2
1.341
0.9863
1.341
X10-3
Kilogram-calories
per minute
0.2520
1.433
X10-9
3.239
1.943
XIO-2
10.69
1
14.33
10.54
1.433
XIO-2
Kilowatts
1.758
XIO-2
10-10
2.260
XI 0-5
1.356
XI 0-3
0.7457
6977
XI 0-2
1
0.7355
10-3
Metric horsepower
2.390
XIO-2
1.360
3.072
XI 0-5
1.843
XI 0-3
1.014
9.485
XI 0-2
1.360
1
1.360
XI 0-3
Watts
17.58
10-7
2.260
XIO-2
1.356
745.7
69.77
1000
735.5
1
1 Cheval-vapeur = 75 kilogram-meters per second
1 Poncelet = 100 kilogram-meters per second
*The "horsepower" used in these tables is equal to 550 foot-pounds per second by definition.
Other definitions are one horsepower equals 746 watts (XI. S. and Great Britain) and one horsepower
equals 736 watts (continental Europe). Neither of these latter definitions is equivalent to the first;
the "horsepowers" defined in these latter definitions are widely used in the rating of electrical
machinery.
Table 18. Quantity of Electricity and Electric Flux [Q]
Multiply
V. Number
Obtain ^^Os>;
Ab coulombs
Ampere-
hours
Coulombs
Faradays
Stat-
coulomba
Abcoulombs *
1
360
0.1
9649
3.335
x 10-11
Ampere-hours
2.778
XI 0-3
1
2.778
xi o-^
26.80
9.259
XI 0-"
Coulombs
10
3600
1
9.649
xio*
3.335
x 10-10
Faradays
1.036
XI 0-*
3.731
XIO-2
1.036
XI 0-6
1
3.457
X 10-16
Statcoulombs *
2.998
XI Oio
1.080
XI 013
2.998
X109
2,893
1
* Conventionally in the electrostatic and electromagnetic systems of units the number of 1inM /
electnc flux emanating from a point charge is 4* times that charge (or quantity of e^StrTcitvlTh I
statcoulomb and the abcoulomb are units of charge not flux viuauwiy 01 electricity;, ine
CONVERSION TABLES
1-59
Table 19. Charge per Unit Area and Electric Flux Density
Multiply
Number
.x/^^x. °f"^
Abcoulombs
Coulombs
Coulombs
Statcoulombs
Coulombs
to^-^v.
per square
centimeter *
per square
centimeter
per square
inch
per square
centimeter
per square
meter
Obtain ^^^^^
Abcoulombs per square centi-
centimeter *
1
0.1
1.550X10~2
3.335X1Q-11
10~5
Coulombs per square
centimeter
10
1
0.1550
3.335X10"10
io-4
Coulombs per square inch
64.52
6.452
1
2.151 X10~9
6.452X10~4
Statcoulombs per square
centimeter *
2.998X1010
2.998X109
4.647X108
1
2.998 X105
Coulombs per square meter
105
10*
1550
3.335X10"6
1
* See footnote to Table 18.
Table 20. Electric Current [
Multiply
Numbet
of-»
Abamperes
Amperes
Statamperes
Abamperes
0.1
3.335 X 10~n
Amperes
10
I
3.335 X 10~10
Statamperes
2.998 X 1010
2.998 X 109
1
Table 21. Current Density
Multiply
-x. Number
^^v^^ of-*
Abamperes
Amperes
Amperes
Statamperes
Amperes
to^^X^
per square
centimeter
per square
centimeter
per square
inch
per square
centimeter
per square
meter
Obtain ^^\o^>
Abamperes per square
1
0.1
1.550X10~2
3.335 X 10~u
IO"6
centimeter
Amperes per square
centimeter
10
1
0.1550
3.335X10~10
,o-4
Amperes per square inch
64.52
6.452
1
2J51X10-*9
6.452X10~4
Statamperes per square
2.998X1010
2.998X109
4.647X108
1
2.998X105
centimeter
Amperes per square meter
IO6
IO4
1550
3.335X10~6
1
1-60 MATHEMATICS; UNITS, AND SYMBOLS
Table 22. Electric Potential and Electromotive Force {M Q-ltfT~z] or [FQ"1L]
Multiply
•s. Number
Obtain ^^^Ov^
Abvolts
Microvolts
Millivolts
Statvolts
Volts
Abvolts
1
100
105
2.998
XI do
108
Microvolts
0.01
1
1000
2.998
XI03
108
Millivolts
10-5
0.001
1
2.998
X105
1000
Statvolts
3.335
3.335
3.335
XIO-6
1
3.335
xio-»
Volts
10-8
10-6
0.001
299.8
1
Table 23. Electric Field Intensity and Potential Gradient [MQ-1LT~^] or [FQ~l]
\ Multiply
\ \Number
Abvolts
per
centi-
meter
Micro-
volts
per
meter
Milli-
volts
per
meter
Statvolts
per
centi-
meter
Volts
per
centi-
meter
Kilo-
volts
per
centi-
Volts
per
inch
Volts
per
mil
Volts
per
meter
Obtain \V
meter
4> ^
Abvolts per
1
1
1000
2.998
108
10u
3.937
3.937
10°
centimeter
XIO10
xio7
X 1010
Microvolts per
I
1
1000
2.998
108
10U
3.937
3.937
106
meter
XlQi°
xio7
X 1010
Millivolts per
0.001
0.001
1
2.998
105
10s
3.937
3.937
1000
meter
xio7
X 104
xio7
Statvolts per
3.335
3.335
3.335
1
3.335
3.335
1.313
1.313
3.335
centimeter
x 10
x io~u
X10~8
X10~3
X I0~5
Volts per
centimeter
10-
10-
10~5
299.8
1
1000
0.3937
393.7
10~2
Klovolts per
centimeter
10-11
10-11
10-8
0.2998
0.001
1
3.937
X I Or*
0.3937
JQ-5
Volts per inch
2.540
XIO"8
2.540
X 10"8
2.540
X 10~5
761.6
2.540
2540
1
1000
2.540
X 10"2
Volts per mil
2.540
x 10-11
2.540
X 10~11
2.540
0.7616
2.540
xio-3
2.540
0.001
1
2.540
X 10~5
Volts per meter
10"6
10-6
10 3
2.998
100
105
39.37
3.937
j
XIO4
xio4
CONVERSION TABLES
Table 24. Electric Resistance [MQ~2L2T~ll or [FQ~*LT\
1-61
Multiply
,. Number
Obtain ^^^$^1
Abohma
Megohms
Microhms
Ohms
Statohms
Abohms
\
1015
1000
109
8.988
X1020
Megohms
10-15
1
10-12
10-6
8.988
X105
Microhms
0.001
1012
1
106
8.988
XI 017
Ohms
10-9
106
10-6
1
8.988
xi on
Statohms
1.112
XI 0-21
1.112
X10-6
1.112
XI 0-18
1.112
XI 0-"
I
Electrical Conductance [F^1QL
1 mho = 1 ohm"1 == 10~6 megmho = 10s micromho
Table 25. Electric Resistivity * [MQ~2LZT~-1] or [FQ~*L*T]
Multiply
V. Number
Obtain ^^O^,
Abohm-
centimeters
Microhm-
centi-
meters
Microhm-
inches
Ohms
(mil, foot)
Ohms
(meter,
gram) t
Ohm-
meters
Abohm-centimeters
'
1000
2540
166.2
s
,0u
Microhm-centimeters
0.001
1
2.540
0.1662
]00
8
108
Microhm-inches
3.937X 10~4
0.3937
1
6.545X 10~2
39.37
5
3.937X 107
Ohms (mil, foot)
6.015 X 10~3
6.015
15.28
1
601.5
S
6.015 X 108
Ohms (meter, gram) f
10-«
0.015
2.540
X 10-25
1.662
X 10~35
1
10-,
Ohm-meters
io-n
10-8
2.540X 10~8
1.662X10"9
10-6
5
1
* In this table S is density in grams per cm.3 The following names, corresponding respectively to those at the tops
of columns, are sometimes used: abohms per cm cube; microhms per cm cube; microhms per inch cube; ohms per mil-
foot; ohms per meter-gram. The first four columns are headed by units of volume resistivity, the last by a unit of mass
resistivity. The dimensions of the latter are Q~*L6T~l; not these given in the heading of the table.
t One ohm (meter, gram) = 5710 ohms (mile, pound).
1-62
MATHEMATICS, UNITS, AND SYMBOLS
Table 26. Electric Conductivity* [M^Q^L^T] or [F~1Q2L~*T
Multiply
. Number
>^\1
Abmhos
per cm
Mhos
(mil, foot)
Mhos
(meter,
gram)
Micro-
mhos
per cm
Micro-
mhos
per inch
Mhos
per
meter
Obtain r^^^sj
Abmhos per cm
1
6.015
10~55
0.001
3.937
,0~n
X 10~3
X 10 4
Mhos (mil, foot)
166.2
1
1.662
0.1662
6.524
1.662
X 10~35
X 10~2
x io~9
Mhos (meter, gram)
105/5
60 1 . 5/5
1
100/5
39.37/5
10- '/«
Micromhos per cm
1000
6.015
0.015
1
0.3937
I0~8
Micromhos per inch
2540
15.28
2.540
2.540
1
2.54
X 10~25
X 10~8
Mhos per meter
1011
6.015
1065
108
3.937
1
X 108
X 107
* See footnote of Table 25, Electric Resistivity. Names sometimes used are abmho per cm cube,
mho per mil-foot, etc. Dimensions of mass conductivity are Q2IT"6T.
Table 27. Capacitance [M-iQ*L~2T2] or [
Abfarada
Farads
Microfarads
Statfarada
Abfarada
10-9
10-15
1.112
X 10-21
Farads
109
10-e
1.112
X 10-12
Microfarads
Statfarads
1015
106
8.988
X 1020
8.988
8.988
X 105
1.112
X 10-fi
CONVERSION TABLES
Table 28. Inductance [MQ~ZLZ] or [FQ~*LT*]
1-63
Multiply
Abhenrys *
IO9
1000
IO6
8.988
X IO20
Henrys
io
10~6
0.001
8.988
X IO11
Microhenrys
0.001
IO6
1000
8.988
X IO17
Millihenrys
10~6
1000
0.001
8.988
X IO14
Stathenrys
1.112
X 10~2>
1.112
X 10~12
1.112
X 10~18
1.112
X 10~15
* An abhenry is sometimes called a "centimeter." See footnote to Table 30 on "Magnetic Flux
Density."
Table 29. Magnetic Flux
Multiply
Number
Kilolines
Maxwells
(or lines)
Webers
Kilolines
0.001
106
Maxwells (or lines)
1000
Webers
10-s
10-8
Table 30. Magnetic Flux Density [MQ^T^] or
Multiply
-x^^^ Number
Obtain ^^O^L.
Gausses
(or lines
per square
centimeter)
Lines per
square inch
Webers
per square
centimeter
Webers
per square
inch
Webers
per square
meter
Gausses (or lines per
1
0.1550
IO8
1.550
IO4
square centimeter)
X IO7
Lines per square inch
6.452
1
6.452
IO8
6.452
X 10s
X IO4
Webers per square
i<r8
1.550
1
0.1550
10-4
centimeter
x io~9
Webers per square inch
6.452
10~8
6.452
1
6.452
X 10~8
X 10~4
Webers per square meter
io-4
1.550
IO4
1550
1
X 10~6
1-64 MATHEMATICS, UNITS, AND SYMBOLS
Table 31. Magnetic Potential and Magnetomotive Force [Qf1]
Multiply
Number
Abampere-turns
Ampere-turns
Gilberts
Abampere-turns
0.1
7.958 X 10-2
Ampere-turns
10
0.7958
Gilberts
12.57
1.257
Table 32. Magnetic Field Intensity, Potential Gradient, and Magnetizing Force [QL 1T l]
Multiply
Number
Abampere-
turns per
centimeter
Ampere-
turns per
centi-
meter
Ampere-
turns per
inch
Oersteds
(gilberts
per centi-
meter)
Ampere-
turns per
meter
Abampere-turns per centimeter
0.1
3.937
X 10~2
7.958
X 10~2
Ampere-turns per centimeter
0.3937
0.7958
Ampere-turns per inch
25.40
2.540
2.021
2.54
X 10~2
Oersteds (gilberts per centimeter)
12.57
1.257
0.4950
1.257
X 10~2
Ampere-turns per meter
103
102
39.37
79.58
Table 33. Specific Heat
(t = temperature)
To convert specific heat in any unit given to any other unit multiply the number of original units
by a factor obtained by dividing the factor in the last column for the final unit by the factor for the
original unit.
Unit of Heat or Energy
Unit of Mass
Temperature Scale*
Factor
Gram-calories
Gram
Kilogram.
Pound
Pound
Gram
Pound
Kilogram
Pound
Centigrade
Centigrade
Centigrade
Fahrenheit
Centigrade
Fahrenheit
Centigrade
Fahrenheit
1
1
1.800
1.000
4.186
1055.
1.163 X 10-8
2.930 X 10~*
Kilngrrftm-fifl.lnripR. T ,.,,,.,.. , . . , . .
British thermal units
Joules ,
Kilowatt-hours
Kilowatt-hours
* Temperature conversion formulas:
tc s= temperature in Centigrade degrees
tf = temperature in Fahrenheit degrees
1 deg fahr = (§6) deg cent.
- 32)
CONVERSION TABLES
1-65
Table 34. Thermal Conductivity [MLT~^-1] and Thermal Resistivity [M-lL~lT*t]
(t = temperature)
To convert thermal conductivity, in gram-calories transmitted per second from one face of a cube
1 cm on edge to the opposite face per degree centigrade temperature difference between these faces,
to the units given in any line of the following table, multiply by the factor in the last column.
To convert thermal conductivity in any unit given to any other unit multiply the number of original
units by a factor obtained by dividing the factor in the last column for the final unit by the factor for
the original unit.
To convert thermal resistivity, in degrees centigrade between one. face of a cube 1 cm on edge and
the opposite face per gram-calories transmitted per second between these faces, to the units given in
any line of the following table, divide by the factor in the last column.
To convert thermal resistivity in any given unit to any other unit multiply the number of the original
units by a factor obtained by dividing the factor in the last column for the original unit by the factor
for the final unit.
Surface emission resistance in thermal ohms per square centimeter is derived from degrees f ahrenheit
per Btu per hour per square foot by multiplying the number of the latter units by 1761.
Units of
Temperature
Scale
Factor
Heat
Area
Thickness
Time
Gram-calories
cm2
m2
ft2
cm2
ft2
m2
ft2
cm
cm
inch
cm
inch
cm
inch
second
hour
hour
second
second
hour
hour
Centigrade
Centigrade
Fahrenheit
Centigrade
Fahrenheit
Centigrade
Fahrenheit
1
3.6 X 104
2903.
4.186
850.6
41.86
0.8506
TCi 1 ogrftm -Oftl oripR
Joules * ...
Kilowatt-hours . ....
Kilowatt-hours
* Thermal resistances in these units are known as thermal ohms.
Table 35. Light
Multiply
^ Number
^\T of-^
Inter-
national
candles
Hefners
10-cp
pentanes
Carcels
Bougie
deci-
males
English
candles
German
candles
Obtain ^^\J
4- >±
International candles
1.00
0.90
10.0
9.61
1.00
1.04
1.055
Hefners
1.11
1.00
11.1
10.66
1.11
1.154
1.17
10-cp pentanes
0.10
0.09
1.00
0.96
0.10
0.104
0.105
Carcels
0.104
0.094
1.04
1.00
0. 104
0.1
0.109
Bougie decimales
1.00
0.90
10.0
9.61
1.00
1.04
1.055
English candles
0.96
0.864
9.6
9.24
0.96
1.00
1.02
German candles
0.95
0.855
9.5
9.19
0.95
0.98
1.00
1-66 MATHEMATICS, UNITS, AND SYMBOLS
18. GAGES
SHEET METAL GAGES. The important sheet metal gages in use in the United States
are- the United States Standard Gage for sheet and plate iron and steel, the American
Wire Gage (also called the Brown and Sharpe W.G.) for copper, aluminum, and brass and
other non-ferrous alloys, the Tin Plate Gage, the Galvanized Sheet Gage, the American
Zinc Gage, and the Birmingham Wire (or Stubs' Iron Wire) Gage. In Canada and Eng-
land the Birmingham Gage (different from the Birmingham Wire Gage) and tho Imperial
Standard Wire Gage (S.W.G.) are used. Still other gages are used elsewhere. In Japan
standard thickness of sheet metal is denoted by the thickness in millimeters. A standard
Decimal Gage, in which the standard thicknesses are denoted by decimal parts of an
inch and not^by gage numbers, has been used in the United States. Copper sheets may
be obtained with thicknesses any integral multiple of Vie of an inch up to 2 in. Heavy
copper sheets may be obtained in definite weights per square foot. Each ounce of weight
is equivalent to approximately 0.001352 in. thickness. Lead is usually ordered in this
manner, each pound being equivalent to approximately 0.017 in. thickness.
The United States Standard Gage for sheet iron and steel (Act of Congress, March 3,
1893; formerly the legal standard for duties) is a weight gage based on a density for wrought
iron of 480 pounds per cubic foot. Since 1893, steel (density of 489.6 Ib per cu ft) has
come into general use. A given gage number of this gage represents a fixed weight per
unit area; hence a steel sheet will have a smaller thickness than a wrought iron sheet of
the same gage number. Monel metal sheets are rolled to the thickness given for wrought
iron without regard to its weight, which is about 552.2 Ib per cu ft. Practice among steel
manufacturers is irregular, some keeping the thickness constant for a given gage number
irrespective of weight. If this practice is followed, the weight per square foot and per
square meter given in the second and third columns of Table 36 will vary, whereas thick-
ness will remain near that given for wrought iron.
The American Wire Gage specifies thicknesses without regard to weight. For the
basis of this gage see Wire Gages, p. 1-70, where are also given the Birmingham W.G
and the S.W.G.
Tables of Thickness and Weight corresponding to United States Standard gage and
American Wire gage numbers are shown in Tables 36 and 37. These tables are taken
from Circular 391 of the Bureau of Standards, in which are given all the gages mentioned
above and the tolerances customary in commerce.
WIRE GAGES. The sizes of wires having a diameter less than 1/2 in. are usually stated
in terms of certain arbitrary scales called "gages." The size or gage number of a solid
wire refers to the cross-section of the wire perpendicular to its length; the size or gage
number of a stranded wire refers to the total cross-section of the constituent wires, irre-
spective of the pitch of the spiraling. Larger wires are usually described in terms of their
area expressed in circular mils. A circular mil is the area of a circle 1 mil in diameter, and
the area of any circle in circular mils is equal to the square of its diameter in mils.
There are a number of wire gages in use, the principal ones being the following:
American or Brown and Sharpe Wire Gage. This gage is the one commonly used in
the United States for copper, aluminum, and resistance wires. The gage is designated by
either of the abbreviations A.W.G. or B. & S.
Basis of the A.W.G. or B. & S. Gage. The diameters of wires having successive num-
bers on this gage are in the ratio of V92( « 1.1229 approx.) to 1, and the No. 36 wire has
a diameter of 5 mils. No. 35 A.W.G., therefore, has a diameter of 5 X 1.1229 « 5.61 mils,
and so on until No. 0000 is reached, having a diameter of 460 mils.
The ratio V^92 is approximately equal to V^, which is 1.1225. This circumstance
makes it possible to have a group of wires of regular gage size with an aggregate area
approximately equal to that of another regular gage size. For example, a reduction of
three gage numbers (as from gage No. 36 to No. 33) results in a new gage number repre-
senting a diameter approximately V% times that represented by the original gage num-
ber— or an area approximately two times as great.
The following approximate relations are also useful:
An increase of 1 in the number increases the resistance 25 per cent.
An increase of 2 in the number increases the resistance 60 per cent
An increase of 3 in the number increases the resistance 100 per cent.
An increase of 10 in the number increases the resistance 10 times
GAGES
1-67
Table 36. United States Standard Gage * for Sheet and Plate Iron and Steel, and Its
Extension f
Gage No.
Weight
per square foot
Weight
per
square
meter
Approximate thickness
Wrought iron
480 Ib/ft*
Steel and open-
hearth iron
489.6 Ib/ft*
Ounces
Pounds
kg
Inch
mm
Inch
mm
0000000....
000000.. ..
320
300
280
260
240
220
200
180
170
160
150
140
130
120
110
100
90
80
70
60
50
45
40
36
32
28
24
22
20
18
16
14
12
11
10
9
8
7
6V2
6
51/2
5
41/2
41/4
4
33/4
31/2
33/8
31/4
31/8
3
20.00
18.75
17.50
16.25
15.00
13.75
12.50
11.25
10.62
10.00
9.375
8.750
8.125
7.500
6.875
6.250
5.625
5.000
4.375
3.750
3.125
2.812
2.500
2.250
2.000
1.750
1.500
1.375
1.250
1.125
1.000
.8750
.7500
.6875
.6250
.5625
.5000
.4375
.4062
.3750
.3438
.3125
.2812
.2656
.2500
.2344
.2188
.2109
.2031
.1953
.1875
97.65
91.55
85.44
79.34
73.24
67.13
61.03
54.93
51.88
48.82
45.77
42.72
39.67
36.62
33.57
30.52
27.46
24.41
21.36
18.31
15.26
13.73
12.21
10.99
9.765
8.544
7.324
6.713
6.103
5.493
4.882
4.272
3.662
3.357
3.052
2.746
2.441
2.136
1.983
.831
.678
.526
.373
.297
.221
.144
.068
1.030
.9917
.9536
.9155
0.500
.469
.438
.406
.375
.344
.312
.2812
.2656
.2500
.2344
.2188
.2031
.1875
.1719
.1562
.1406
.1250
.1094
.0938
.0781
.0703
.0625
.0562
.0500
.0438
.0375
.0344
.0312
.0281
.0250
.0219
.0188
.0172
.0156
.0141
.0125
.0109
.0102
.0094
.0086
.0078
.0070
.0066
.0062
.0059
,0055
.0053
.0051
.0049
.0047
12.70
11.91
11.11
10.32
9.52
8.73
7.94
7.14
6.75
6.35
5.95
5.56
5.16
4.76
4.37
3,97
3.57
3.18
2.778
2.381
.984
.786
.588
.429
.270
1.111
.952
.873
.794
.714
.635
.556
.476
.437
.397
.357
.318
.278
.258
.238
.218
.198
.179
.169
.159
.149
.139
.134
.129
.124
.119
0.490
.460
.429
.398
.368
.337
.306
.2757
.2604
.2451
.2298
.2145
.1991
.1838
.1685
.1532
.1379
.1225
.1072
.0919
,0766
.0689
.0613
.0551
.0490
.0429
.0368
.0337
.0306
.0276
.0245
.0214
.0184
.0169
.0153
.0138
.0123
.0107
.0100
.0092
.0084
.0077
.0069
.0065
.0061
.0057
.0054
.0052
.0050
.0048
.0046
12.45
11.67
10.90
10.12
9.34
8.56
7.78
7.00
6.62
6.23
5.84
5.45
5.06
4.67
4.28
3.89
3.50
3.11
2.724
2.335
1.946
1.751
1.557
1.400
1.245
1.090
.934
.856
.778
.700
.623
.545
.467
.428
.389
.350
.311
.272
.253
.233
.214 ,
.195
.175
.165
.156
.146
.136
.131
.126
.122
.117
00000
oooo
000
00 .
o
1
2
3
4
5
6
7
8
9
10 .
11
12
13
14
15
16
17
18
19
20
21
22
23
24
25..
26
27
28
29 . ...
30
31
32
33
34
35
36
37
38
39
40
41
42
43...
44
* For the Galvanized Sheet Gage, add 2.5 ounces to the weight per square foot as given in the
table. Gage numbers below 8 and above 34 are not used in the Galvanized Sheet Gage.
t Gage numbers greater than 38 were not in the standard as set up by law, but are in general use.
1-68
MATHEMATICS, UNITS, AND SYMBOLS
Table 37. American Wire Gage — Weights of Copper, Aluminum, and Brass Sheets and
Plates
Gage No.
Thickness
Approximate weight * per sq ft in Ib
Inch
JDTYl
Copper
Aluminum
Commercial
(high) brass
0000
0.4600
.4096
.3648
.3249
.2893
.2576
.2294
.2043
.1819
.1620
.1443
.1285
.1144
.1019
,0907
.0808
.0720
.0641
.0571
.0508
.0453
.0403
.0359
.0320
.0285
.0253
.0226
.0201
.0179
.0159
.0142
.0126
,0113
.0100
.00893
.00795
.00708
.00630
.00561
.00500
.00445
.00397
.00353
.00314
11.68
10.40
9.266
8.252
7.348
6.544
5.827
5. 189
4.621
4.115
3.665
3.264
2.906
2.588
2.305
2.053
1.828
1.628
1.450
1.291
1.150
1.024
0.9116
,8118
.7230
.6438
.5733
.5106
.4547
.4049
.3606
.3211
.2859
.2546
.2268
.2019
.1798
.1601
.1426
,1270
.1131
.1007
.0897
.0799
21.27
18.94
16.87
15.03
13.38
11.91
10.61
9.45
8.41
7.49
6.67
5.94
5.29
4.713
4.195
3.737
3.330
2.965
2.641
2.349
2.095
1.864
.660
.480
.318
.170
.045
0.930
.828
.735
.657
.583
.523
.4625
.4130
.3677
.3274
.2914
.2595
.2312
.2058
.1836
.1633
.1452
6.49
5.78
5. 14
4.58
4.08
3.632
3.234
2.880
2.565
2. 284
2.034
1.812
.613
.437
.279
.139
.015
0.904
.805
.716
.639
.568
.506
.451
.402
.3567
.3186
.2834
.2524
.2242
.2002
.1776
.1593
.1410
.1259
.1121
.0998
.0888
.0791
.0705
.0627
.0560
.0498
.0443
20.27
18.05
16.07
14.32
12.75
11.35
10.11
9.00
8.01
7.14
6.36
5.66
5.04
4.490
3.996
3.560
3. 172
2.824
2.516
2.238
.996
.776
.582
.410
.256
.115
0.996
.886
.789
.701
.626
.555
.498
.4406
.3935
.3503
.3119
.2776
.2472
.2203
.1961
.1749
.1555
. 1383
000
00
0 ...
1
2
3
4
5 ...
6
7
8
9
10
11
12
13
14
15
16 ..
17
18
19
20
21
22 ..
23
24 .
25
26 .. . .
27
28
29
30
31
32
33 . . .....
34
35...
36
37
38
39
40
Cubi° centimeter'
•, 8.89; aluminum.
GAGES 1-69
A No. 10 A.W.G. copper wire has the following approximate characteristics:
Ohms per 1000 ft 1
Circular mils area 10,000
Weight, pounds per 1000 ft 32
A No. 10 A.W.G. aluminum wire has the following approximate characteristics:
Ohms per 1000 ft 1.6
Circular mils area 10,000
Weight, pounds per 1000 ft 9.5
Remembering these rules it is easy to find the approximate size, resistance, area, or
weight of any size wire. For example, a No. 12 A.W.G. copper wire has a resistance of
1 plus 60 per cent = 1.6 ohms per 1000 ft approximately. Its area, being inversely as
its resistance, is 10,000/1.6 = 6250 circular mils; its diameter is therefore \/6250 = 79
mils, and its weight 32/1.6 = 20 Ib per 1000 ft.
U. S. Steel Wire Gage. This gage, known also as the "Washburn and Moen," "Roeb-
ling," "American Steel and Wire Co.'s gage," is the one usually employed in the United
States for steel and iron wire. It is frequently abbreviated "S.W.G.," but to avoid con-
fusion with the British Standard Wire Gage (see below] it should be abbreviated "StL
W.G." or "A. (steel) W.G."
Birmingham (or Stubs' Iron) Wire Gage. This gage is still used in the United States
for some purposes, e.g., to designate the size of brass wire, and is also employed to a
limited extent in Great Britain. It is usually abbreviated "B.W.G." It is sometimes
referred to as the "Stubs' Iron Wire Gage," but it should not be confused with the Stubs'
Steel Wire Gage.
British Standard Wire Gage. This gage, usually called simply the * 'Standard Wire
Gage" and abbreviated "S.W.G.," is also known as the "New British Standard" (ab-
breviated "N.B.S."), the English Legal Standard, or the Imperial Wire Gage, and is the
legal standard of Great Britain for all wires, as fixed by order in Council, August 23, 1883.
It was constructed by modifying the Birmingham Wire Gage, so that the differences be-
tween successive diameters were the same for short ranges, i.e., so that a graph representing
the diameters consists of a series of a few straight lines.
Edison Wire Gage. The size of a wire on this gage is equal to its cross-sectional area
in circular mils divided by 1000. For example, a solid wire 0.2 in. in diameter has the
number (200)2/1000 = 40. This gage is now rarely used.
Metric Wire Gage. The gage number is ten times the diameter in millimeters.
Other Gages. In addition wire sizes are sometimes specified in terms of the "Old
English Wire Gage," known also as the "London Gage," and the "Stubs' Steel Wire
Gage." The Old English Wire Gage is the same as B.W.G. for all gage numbers under 20.
Comparison of Wire Gages. A comparison of the different gages, in terms of the diam-
eters (in mils or thousandths of an inch) of solid wires corresponding to the various num-
bers, is given in Table 38. The cross-section in circular mils is the square of the diameter
in mils.
1-70 MATHEMATICS, UNITS, AND SYMBOLS
Table 38. Comparison of Wire Gage Diameters in Mils
(Bureau of Standards, Circulars 31 and 67)
Gage
No.
America
wire
gage
(B. &S
Steel
wire
gage
Birming
ham wir
gage
(Stubs'
Old
English
wire gag
(London
Stubs'
steel
wire
gage
(British
Standarc
wire
gage
Metric
gage *
Gage
No.
7-0
6-0
5-0
4-0
3-0
2-0
0
1
2
3
4
5
6
7
8
9
10
11
12
13
14
15
16
17
18
19
20
21
22
23
24
25
26
27
28
29
30
31
32
33
34
35
36
37
38
39
40
41
42
43
44
45
46
47
48
49
50
490.0
461.5
430.5
393.8
362.5
331.0
306.5
283.0
262.5
243.7
225.3
207.0
192.0
177.0
162.0
148.3
135.0
120.5
105.5
91.5
80.0
72.0
62.5
54.0
47.5
41.0
34.8
31.7
28.6
25.8
23.0
20.4
18.1
17.3
16.2
15.0
14.0
13.2
12.8
11.8
10.4
9.5
9.0
8.5
8.0
7.5
7.0
6.6
500
464
432
400
372
348
324
300
276
252
232
212
192
176
160
144
128
116
104
92
80
72
64
56
48
40
36
32
28
24
22
20
18
16.4
14.8
13.6
12.4
11.6
10.8
10.0
9.2
8.4
7.6
6.8
6.0
5.2
4.8
4.4
4.0
3.6
3.2
2.8
2.4
2.0
1.6
1.2
7-0
6-0
5-0
4-0
3-0
2-0
0
1
2
3
4
5
6
7
8
9
10
11
12
13
14
15
16
17
18
19
20
21
22
23
24
25
26
27
28
29
30
31
32
33
34
35
36
37
38
39
40
41
42
43
44
45
46
47
48
49
460
410
365
325
289
258
229
204
182
162
144
128
114
102
91
81
72
64
57
51
45
40
36
32
28.5
25.3
22.6
20.1
17.9
15.9
14.2
12.6
11.3
10.0
8.9
8.0
7.1
6.3
5.6
5.0
4.5
4.0
3.5
3.1
454
425
380
340
300
284
259
238
220
203
180
165
148
134
120
109
95
83
72
65
58
49
42
35
32
28
25
22
20
18
16
14
13
12
10
9
8
7
5
4
454
425
380
340
300
284
259
238
220
203
180
165
148
134
120
109
95
83
72
65
58
49
40
35
31.5
29.5
27.0
25.0
23.0
20.5
18.75
16.50
15.50
13.75
12.25
11.25
10.25
9.50
9.00
7.50
6.50
5.75
5.00
4.50
227
219
212
207
204
201
199
197
194
191
188
185
182
180
178
175
172
168
164
161
157
155
153
151
148
146
143
139
134
127
120
115
112
110
108
106
103
101
99
97
95
92
88
85
81
79
77
75
72
3.94
7.87
11.8
15.7
19.7
23.6
27.6
31.5
35.4
39.4
47.2
55.1
63.0
70.9
78.7
98.4
118
138
157
6.2
6.0
5.5
177
5.2
4.8
4.6
A A
* For diameters corresponding to metric ca
those of 12, 14, etc., by tea.
ov
ge numbers, 1.2, 1.4, ]
1.0
.6, 1.8, 2.5
197
3.5, and 4
.5, divide
ABBREVIATIONS FOR ENGINEERING TERMS
1-71
SYMBOLS AND ABBREVIATIONS
19. ABBREVIATIONS FOR ENGINEERING TERMS
NOTE: This list is a selection of American Tentative Standard abbreviations, for scientific and
engineering terms, recommended by the American Standards Association. (See ASA, Z10.1 — 1941.)
Absolute abs
Acre spell out
Alternating-current (as adjective) ac
Ampere amp
Ampere-hour amp-hr
Angstrom unit A
Atmosphere atm
Atomic weight at. wt.
Average avg
Avoirdupois avdp
Barometer bar.
Barrel bbl
Baume1 Be"
Boiler pressure spell out
Boiling point bp
Brake horsepower bhp
Brake horsepower-hour bhp-hr
Brinell hardness number Bhn
British thermal unit Btu or B
Calorie cal
Candle c
Candle-hour c-hr
Candlepower cp
Centigram eg
Centiliter cl
Centimeter cm
Centimeter-gram-second (system) cgs
Chemically pure '. cp
Circular cir
Circular mils cir mils
Coefficient coef
Cologarithm colog
Concentrate cone
Conductivity cond
Constant , const
Cord cd
Cosecant esc
Cosine cos
Cotangent cot
Coulomb spell out
Counter electromotive force cemf
Cubic cu
Cubic centimeter cu crn, cm3, cc
Cubic feet per minute cfm
Cubic foot cu f t
Cubic inch cu in.
Cubic meter cu m or m3
Cubic yard cu yd
Cycles per second spell out or c
Decibel db
Degree deg or °
Degree Centigrade C
Degree Fahrenheit F
Degree Kelvin K
Degree Reaumur R
Diameter diam
Direct-current (as adjective) d-c
Dozen doz
Dram dr
Efficiency eff
Electric elec
Electromotive force emf
Equation eq
External ext
Farad spell out or f
Foot ft
Foot-candle f t-c
Foot-Lambert f t-L
Foot-pound f t-lb
Foot-pound-second (system) fps
Freezing point fp
Fusion point fnp
Gallon gal
Grain spell out
Gram g
Gram-calorie g-cal
Henry h
Horsepower hp
Horsepower-hour hp-hr
Hour hr
Hundred C
Hyperbolic sine sinh
Hyperbolic cosine cosh
Hyperbolic tangent tanh
Inch in.
Inch-pound in-lb
Internal int
Joule j
Kilocycles per second kc
Kilogram kg
Kilogram-calorie kg-cal
Kilogram-meter kg-m
Kiloliter Id
Kilometer km
Kilovolt kv
Kilovolt-ampere kva
Kilowatt kw
Kilowatthour kwhr
Lambert L
Latitude lat or <f>
Linear foot lin ft
Liter 1
Liquid liq
Logarithm (common) log
Logarithm (natural) loge or hi
Longitude long, or X
Lumen 1
Lumen-hour 1-hr
Magnetomotive force mmf
Maximum max
Melting point mp
Meter m
Meter-kilogram m-kg
Mho spell out
Microampere Ma or mu a
Microfarad /if
Micromicron ij.fi or mu mu
Micron M or mu
Microwatt MW or mu w
Mile spell out
Milliampere ma
Milligram mg
Millihenry , mh
1-72
MATHEMATICS, UNITS, AND SYMBOLS
Abbreviations for Engineering Terms— Continued
Milliliter ml
Millimeter mm
Millimicron
Million
Millivolt P™
Mean horizontal eandlepower mncp
Miles per hour , mPh
Minimum •
Minute •
Minute (angular measure)
Qkm spell out or £2
Ounce
Ounce-foot
Ounce-inch
or m mu
sPeU out
mm
min
oz'ltl
oz-in-
Pint
Potential ........................... speU out
Pound .................................. • £
Pound-foot ............................ Tilb:±t;
Pound-inch ........................... lb-m-
Pounds per square foot ................... psi
Pounds per square inch ................... PS1
Power factor .................. spell out or pf
Quart ................................... <#
Radian ............................ sPeU out
Reactive kilovolt-ampere ................ kvar
Reactive volt-ampere .................... var
Revolutions per minute .................. rPm
Revolutions per second ................... rPs
Root mean square ....................... rms
see
sec
SP
Secant
Second ............
Second (angular measure)
Sine
Specific gravity
Specific heat ...........................
Spherical candlepower .................... SCP
Square .................................. acj
Square centimeter .............. sq cm or cm2
Square foot ............................ 8flft
Square inch ....................... •••• S(J m£
Square kilometer .............. «Q ^m or km
Square meter ..................... Bq in or m<
Square micron ............ sq ^ or sq mu or ^
Square root of mean square ............... rms
Standard .............................. sfcd
Tangent ............................... • tan
Temperature .......................... temP
Thousand .............................. • M
Ton ............................... 8Pe11 oufc
Versed sine ............................. VGrs
Volt ..................................... v
Volt-ampere ............................. va
Watt .................................... w
Watthour .............................. whr
Weight ................................. wt
Yard ................................... 3rd
Year .................................... V*
20. LETTER SYMBOLS FOR THE MAGNITUDES OF
ELECTRICAL QUANTITIES
(Tentative American Standard Z10.5-1947) t
In the alphabetical order of the names of the quantities
Each quantity appears at only one place in this table (with a few exceptions), listed
alphabetically under its preferred name. The non-preferred names appear in parentheses
under the preferred names. Deprecated names are also in parentheses and in addition
are asterisked thus: (electric force)*.
Names beginning with the qualifying adjectives, electric, electrostatic, dielectric, magnetic,
mutual, self, and relative, are listed under the term that is so qualified.
Symbols for scalar quantities, whose values are expressed by real numbers, are printed
in ordinary-face italic letters.
Symbols for vector quantities are printed in "bold-face Roman letters.
Symbols for phasor quantities, whose values are expressed by complex numbers, are
printed in bold-face italic letters.
Item
Quantity
Symbol
Item
Quantity
Symbol
1
admittance
y
7
line d. of charge
X
2
attenuation constant
a
8
surface d, of charge
<r
3
capacitance
C
9
volume d. of charge
P
(capacity) *
10
conductance
O
(permittance) *
11
conductivity
y
4
capacitivity
6
12
conductivity,
A
dielectric constant
equivalent
(permittivity) *
13
coupling coefficient
k
of evacuated space
«T
14
current
I
5
capacitivity, relative
*r
(intensity of current) *
relative dielectric constant
15
current density
(specific inductive capacity) *
16
sheet c.d. (linear c.d.)
A
6
charge, electric or quantity of
Q
17
damping constant or coefficient
8
electricity
(decay constant)
charge density
* Deprecated name.
f Reprinted by permission of the American Institute of Electrical Engineers.
LETTER SYMBOLS FOR ELECTRICAL QUANTITIES 1-73
Letter Symbols for the Magnitudes of Electrical Quantities — Continued
Item
Quantity
Symbol
Item
Quantity
Symbol
18
dielectric constant
£
50
phase constant
(3
see capacitivity
wavelength constant
dielectric, a qualifier
(wave number)
see term that it qualifies
51
polarization, electric
19
displacement, electric
D
52
polarization, magnetic
Bi
20
efficiency
f]
intrinsic induction
21
elastance
S
metallic induction
mutual e. Sm, Src
53
pole strength
m
self e. 8, Soc
54
potential, electric
V
22
elastivity
ff
(electromagnetic scalar p.)
electric, a qualifier
55
potential, retarded scalar
see term that it qualifies
56
potential, magnetic
M,&
23
electronic charge
e
(magnetic scalar p.)
(absolute value of)
m. pot. difference
24
electromotive force
E
57
potential, magnetic vector p.
A
(electromotance)
58
potential, retarded vector p.
A.r
(potential difference, electric)
59
power, active
P
(voltage) *
60
power, reactive
Q
25
energy
W
volt-amperes, reactive
26
force
F
61
power, apparent
S
27
flux, displacement f.
^
volt-amperes
(flux of e. displacement)
62
power factor
Fp
28
flux, magnetic
$
63
propagation constant
7
(flux of magnetic induction)
64
Poynting vector
1 n
29
flux-linkage
65
quantity of electricity
Q
30
frequency
/
charge, electric
'31
frequency, angular
CO
66
quality factor of a reactor
Q
angular velocity
figure of merit of a reactor
32
frequency, rotational
n
67
reactance
X ,
33
impedance
Z
capacitative r.
Xc
mutual i. Zm, Zrc
inductive r.
XL
self i. Z, Zcc
mutual r. %m, Xrc
34
induction, magnetic
B
selfr. Z, Zcc
(magnetic flux density)
68
reactive factor
Fq
35
inductance
L
69
reluctance
(R
mutual i. Lm, Lrc
70
reluctivity
v
self i. L, LCC
71
resistance
R
36
intensity, electric
E,K
mutual r. Rm, Rrc
(electric field intensity)
self r. R, Rcc
(electric field strength)
72
resistivity
P
(electric force) *
73
resistance-temperature coefficient
a
(electric field) *
rotative operators
37
intensity, magnetic or magnetiz-
H
74
90°, V- *
j
ing force
75
120°, -\/~\
a
(magnetic field strength)
self, a qualifier
(magnetic force) *
magnetic, a qualifier
76
see term that it qualifies
slip
see term that it qualifies
77
susceptance
S
38
magnetomotive force
M.JF
susceptibility
(m. potential difference)
78
dielectric s.
y
39
magnetomotance
moment, electric
P
79
intrinsic capacitivity
magnetic s.
K
40
41
42
moment, magnetic
number of conductors or turns
number of poles
m
N
P
80
81
intrinsic permeability
symmetrical components (Note 5)
temperature
43
number of phases
m
T, (0)
44
period
T
82
time
i
45
permeance
<P, A
83
time constant
T
46
permeability, magnetic
of evacuated space
to
84
85
velocity of light
vibration constant
c
P
47
48
permeability, relative
(permittivity) * (see capacitivity)
Mr
86
(oscillation constant)
wavelength
X
49
phase angle
9
87
wavelength constant
phase constant
88
work
W
* Deprecated name.
1-74 MATHEMATICS, UNITS, AND SYMBOLS
Note 1. Designation of maximum, instantaneous, rms, and average values.
Where distinctions between maximum, instantaneous, root-mean-square (effective), and
average values are necessary, Emt Im, Qw, and Pm are recommended for maximum values;
e, t, #, and p for instantaneous values, E, I, and Q for root-mean-square values and £,a, /0,
Qa, and P for average values.
Note 2. Quantities per unit volume, area, or length.
It is recommended that quantities per unit volume, area, length, etc., be represented as
far as practicable by lower-case letters corresponding to the cap letters which represent the
total quantities, or by the cap letters with the subscript 1, except for those quantities for
which this table has symbols for the quantity per unit volume, area, etc.
Note 3. Distinction between the symbols V and E for potential and electromotive force.
The distinction between the use of V for potential and E for electromotive force is :
V is to be used for potentials or potential differences that are attributed solely to that
distribution of electric field intensities which is computed (by the inverse square law of
force) from the segregated charges of the field.
E is to be used for the emf along a path from a terminal A to a terminal B when in the
region A to B one or more non-electrostatic types of electric intensities exist, or turbulent
actions occur — as in voltaic cells, electrostatic generators, and electromagnetic sources of
emf.
Note 4. The sequence of the double subscripts to multiplying operators.
The sequence of the double subscripts to the multiplying operators (mutual impedances,
resistances, or elastances or transconductances, etc.) that occur in the fundamental equa-
tions of networks is to be determined by the following consideration :
Consideration. The set of fundamental equations (e.g., Kirchhoff's emf equations)
should yield a determinant in which the subscript sequence conforms to the mathe-
matician's convention for writing determinants; namely,
Convention. In the double subscripts of the elements of a determinant, the subnumbor
designating the "row" is to precede the subnumber designating the "column" to which the
element belongs, or the order is erc- Thus
This consideration leads to the following rule :
Rule for writing double subscripts.
The first subnumber in the symbol for a multiplying operator designates the number of
the circuit in which the product of the multiplication is measurable, while the second sub-
number designates the number of the circuit in which the operand or multiplicand is
measurable.
As an illustration, Eirchhoff's emf law for the emfs of the rth circuit due to the currents
in all the circuits of a network is written:
Er,d =
(ET,d being the driving emf impressed in the rth circuit) .
Note 5. Notation for symmetrical components.
The standard notation for designating the symmetrical components of the currents and
potential differences in unbalanced polyphase systems is that subscript notation in which:
(a) double subscripts are added to the symbols for current and potential difference;
(b) the first and second subscripts designate, respectively, the phase and the sequence to
which the component belongs;
(c) the first, or phase, subscript may be the phase number, or the phase letter, or a two-
letter combination that designates (on a diagram) both the phase and the direction in
the phase;
(d) the second or sequence, subscript is always to be the number that designates the
sequence to which the component belongs; the positive, negative, and zero sequence com-
ponents in three-phase systems being designated by the numbers 1, 2, and 0, respectively.
Illustration of notation:
la, ~ I al + -Fo2 + IaQ
2b — Ibl + 2 b2 + IbQ
Ic = la. +
1-76
MATHEMATICS, UNITS, AND SYMBOLS
21. STANDARD GRAPHICAL SYMBOLS
(Approved by American Standards Association, Nov. 1, 1942)
(Revised by American War Standard, April 18, 1944)
1. Ammeter
2. Antenna
3. Antenna, Loop
-/A\-
LM
0
17. Jack
18. Key
19. Lightning Arrester
20. Loudspeaker
o * "Vf]
i
=oC]
4. Arc
1<:
21. Microphone
=3
5. Battery
Long line always positive
but polarity may be Indicated
In addition.
H^
22. Phototube
$
6. Capacitor, Fixed — L-
Condenser, Fixed """P*
The curved electrode Identifies
the outermost electrode where applicable
or the negative electrode for electrolytic
capacitors.
7. Ca-pacitor, Fixed, Shielded — -} (
23. Piezoelectric Plate
24. Resistor
25. Resistor, Adjustable or
Variable
-0-
-AAA/V
8. Capacitor, Variable
The curved portion is the
movable electrode.
9. Capacitor, Variable, Shielded
4L
26. Spark Gap, Plain
27. Spark Gap, Quenched
28. Spark Gap, Rotary
-D 0-
-niniiih
_ AA
10. Counterpoise
rh
29. Telephone Receiver
30. Telephone Transmitter
cjcp
=OJ
U. Crystal Detector
12. Galvanometer
•f
31. Thermoelement
32. Transformer, Air Core
_LL
13. Ground J=-
14. Inductor -^rjfftftfX-
15. Inductor, Adjustable or Variable
— onooo — .
33. Transformer, Iron Core.
3C
34. Transformer, with Variable Coupling
iff.
16. Inductor Iron Core
£__ l
-^Tnj^cr^
35. Voltmeter
36. Wires, Crossed, not joined
» * > i my
+
-jam-
37. Wires, Joined
_ru_
STANDARD GRAPHICAL SYMBOLS
l-'J
1. Anode or Plate
(Including Collector)
2. Cathode-Ray Tube wfifh
Electrostatic Deflection
3. Cathode-Ray Tube for
Magnetic Deflection
4. Cold Cathode
(Including Ionic-Heated Caihode)
5. Deflecting, Reflecting, or
Repelling Electrode
(Electrostatic Type)
6. Diode
(Cold-cathode and
Gas Content)
7. Directly Heated Cathode
(Filament Type)
8. Double-Cavity Resonator
Eav.eJope
9. Double-Cavity Velocity-
Modulation Tube with
Collecting Electrode
»10. Dynod'e
11. Excitor
(Contacto'f'T.ype)
Electron Tubes
(ASA 232.10-1944)
14. Beater
12. Gas-Filled Envelope
Located as X^^X
convenient f- >+ \
13. Grid
(including Beam-Confining or
Beam-Forming ELectnodes)
n
15. High-Vacuum Envelope
16. Ignitor
Ignltor
17. Indirectly Heated Cathode
18. Ionic-Heated Cathode with
Supplementary Heater
19. Loop Coupling
(Electromagnetic Type)
20. Mercury Pool Tube with
Excitor, Control Grid, and
Holding Anode
21. Mercury Pool Tube with
Ignitor and Control Grid
22. Pentode
(Suppressor or Beam-
confining Electrodes)
23. Photoelectric Cathojde
24. Phototube
25. Phototube
(Multiplier Type)
Y
1-78 MATHEMATICS, UNITS, AND SYMBOLS
Electron Tubes — Continued
(ASA Z32.10-1944)
26. Pool Cathode
27. Resonant Magnetron
28. Shield within Envelope ( i
External Connection
29. Single-Cavity Resonator
Envelope
30. Single-Cavity Velocity-
Modulation Tube with
Reflecting Electrode
31. Target, X-Ray
32. Transit-Time Split-Plats Type
Magnetron with Stabilizing
Deflecting Electrodes and
Internal Circuit
33. Triode with Filamentary
Cathode
34. Triode with Indirectly
Heated Cathode and
Envelope Connection
35. Triode with Indirectly
Heated Cathode and
Envelope Connected
to Base Terminal
36, Triode-Heptode with Rigid
Envelope Connection
Small Pin
37. Tube Base Terminals
Large Pin
Rigid Terminals
Flexible Leads.
38. Tube Envelope Terminals
39. This figure illustrates
how tube symbols
may be placed in any
convenient position
as shown in a
communication
transformer circuit.
40. General Notes
(a) The diagram for a tube having more than
one heater shall show only one heater symbol
(inverted V) unless the heaters have entirely
separate connections. If a tap Is made, one heater
symbol shall still be shown, and the tap shall be
shown at the vertex of the heater symbol, regardless
of the actual division of voltage across the heater
(6) Item (a) shall apply also to filaments. In
case of a tap, either brought out to a pin connection
or internally connected as to a suppressor grid, the
tap shall be shown at the vertex of the filament
symbol, regardless of the actual division of voltage
across the filament.
(c) A type having more than one cathode shall
be shown as having a single cathode unless separate
cathode connections are made.
(d) A type having two or more grids tied
Internally shall be shown with symbols for each grid,
except when the grids are adjacent in the tube
structure. Thus the diagram for a twin pentode
having a common screen-grid connection for each
section and for a converter tube having the No. 3
and the No. 5 grids connected Internally will show
separate symbols for each grid. However, a trlode
where the control grid Is physically In the form of
two grid windings would show only one grid.
(e) A type having a grid adjacent to a plate but
Internally connected to the plate to form a portion of
it shall be shown as having a plate only,
(/) Associated parts of a circuit such as deflecting
coils, field coils, etc., are not a part of the tube
symbol but may be added to the circuit in the form
of standard symbols as shown in ASA Z32.3 or ASA
Z32.5. For example, resonant-type magnetron plus
symbol for ferromagnetic inductor would be shown
r)
V
Uj&ly —
PRINCIPAL PHYSICAL CONSTANTS AND RATIOS 1-79
22. USE OF GREEK ALPHABET FOR SYMBOLS
Capital
Lower
Case
Name
Commonly Used to Designate
A
a
Alpha
Angles. Area. Coefficients. Attenuation constant.
B
JS
Beta
Angles. Flux density. Coefficients.
r
7
Gamma
Conductivity. Specific gravity. Propagation constant.
A
8
Delta
Variation. Density. Damping coefficient.
E
€
Bpsilon
Base of natural logarithms. Capacitivity.
z
r
Zeta
Impedance. Coefficients. Coordinates.
H
t\
Eta
Hysteresis coefficient. Efficiency.
e
e
Theta
Temperature. Phase angle.
I
i
Iota
K
»
Kappa
Dielectric constant. Susceptibility.
A
X
Lambda
Wavelength.
M
M
Mu
Micro. Amplification factor. Permeability.
N
V
Nu
Reluctivity.
3
£
Xi
0
0
Omicron
n
TT
Pi
Ratio of circumference to diameter = 3. 1 4 1 6.
p
P
Rho
Resistivity.
s
ff
Sigma
Capital: sign of summation.
T
T
Tau
Time constant. Time phase displacement.
T
U
Upsilon
$
$ or <p
Phi
Magnetic flux. Angles.
X
X
Chi
*
t
Psi
Dielectric flux. Phase difference.
ft
CO
Omega
Capital: ohms. Lower case: angular velocity, or 2tr X frequency.
CONSTANTS
By Carl C. Chambers
23. PRINCIPAL PHYSICAL CONSTANTS AND RATIOS *
Velocity of light
Ratio of electrostatic to electromagnetic units .
Volume of a perfect gas (0 deg cent and normal
atmospheric pressure)
Normal atmospheric pressure
45 deg cent atmospheric pressure
Ice point (absolute scale)
Mechanical equivalent of heat (15 deg cent) . .
Electrical equivalent of heat (15 deg cent) ....
Faraday constant
Electronic charge
Planck constant
Acceleration of gravity
Electrochemical equivalent of silver
Wave length of red cadmium line (15 deg cent,
normal atmospheric pressure)
Effective grating space of calcite (18 deg cent)
Avogadro's number
Boltzmann constant
Stefan-Boltzmann constant
Mass of the electron
Ratio of mass of H to mass of electron (meas-
ured by deflection)
(2.99776 db 0.00004) X 1010 cm sec"1
f (2.9971 ± 0.0001) X 1010 <
c"^
(in
\ (2.9978 ± 0.0001) X 1010 cm sec"1 (in absolute units)
(22.4146 ± 0.0006) X 103 cm3 mole"1
(1.013246 db 0.000004) X 106 dynes cm"2
(1.013195 ± 0.000004) X 106 dynes cm"2
273.18 ± 0.01° K
4.1855 ± 0.0004 abs joule cal"1
4.1847 ± 0.0003 int joule cal"^
96494 ± 5 int coulombs g-equiv"1
(4.8025 ± 0.0010) X 10~10 abs-es unit
(1.60203 ± 0.00034) X 10"20 abs-em unit
(6.624 ± 0.002) X 10"27 erg sec
980.665 cm sec"2
1.11800 X 10~3 g. int coulombs"1
6438.4696 I.A. f
3.02904 X 10~8 cm
(6.0228 ± 0.0011) X 1023 mole"1
(1.3708 ± 0.0014) X 10"16 erg deg"1
(5.672 ± 0.003) X 10~5 erg cm-2 deg~4 sec"1
(9.1066 ±0.0032) X KT28 g
1837.5 ± 0.5
* Values taken from Birge, Rev. of Mod. Phys., Vol. 13, No. 4 (October, 1941).
t This defines the international angstrom unit (I. A.). The unit is of the order of 1 part in several
million different from 10~8 cm.
1-80
MATHEMATICS; UNITS, AND SYMBOLS
24. STANDARD RADIO-FREQUENCY RANGES
The International Telecommunication Union in 1947 adopted officially the Nomen-
clature of Frequencies shown in Table 39. The designation of each metric subdivision of
wavelength range is the name of the metric unit of length which is equal to the shortest
wavelength in the range. The range number is the power of 10 which represents the
approximate mean frequency of that range. The frequency subdivision designations are
those first adopted by the Armed Forces of the United States and subsequently by other
branches of the government.
The table is based on the approximation that the wave velocity is 300,000,000 meters
per second. In any case, where the required precision makes this assumption inadequate,
the exact boundaries of the ranges should be based on the frequency range, not the wave-
length range. ., .,• , * •
It is suggested that the term radio be added where there is any possibility of confusion.
A power engineer might be considerably startled to hear 100 kc referred to as a 'low
frequency."
The term microwave has been variously used: (1) as referring to waves less than 1 meter
in length; (2) as certainly including ranges 10 and 11, and part of 9; (3) as referring to
waves using cavities instead of LC tuned circuits; and (4) as referring to waves transmitted
by wave guides. Where any confusion is possible, the term should be eschewed or clarify-
ing text added.
Table 39. Nomenclature of Frequencies
Range
Frequency Range
Wavelength
Range
"Mum
Frequency
J.NUm-
her
Lower
Upper
Lower
Upper
Subdivision
Subdivision
N
Limit
Limit
Limit
Limit
(Inch)
(Excl.)
(Excl.)
CIncl.)
0
0.3 c
3c
I
3c
30 c
2
30 c
300 c
3
300 c
3kc
4
3kc
30 kc
10km
100km
Myriametric waves
VLF (very low frequency)
5
30 kc
300 kc
1km
10km
Kilometric waves
LF (low frequency)
6
300 kc
3,000fcc
Ihm
lOhm
Hectometric waves
MF (medium frequency)
7
3,000kc
30,000 kc
1 dkm
10 dkm
Decametric waves
HF (high frequency)
8
30,000kc
300 Me
1 m
10m
Metric waves
VHF (very high fre-
quency)
9
300 Me
3, 000 Me
1 dm
10dm
Decimetric waves
UHF (ultra high fre-
quency)
10
3,000 Me
30, 000 Me
1 cm
10cm
Centimetric waves
SHF (super high fre-
quency)
11
30,000 Me
300 kMc
1 mm
10mm
Millimetric waves
EHF (extremely high fre-
quency)
12
300 kMc
3,000 kMc
13
3,000 kMc
30,000 kMc
14
30, 000 kMc
300 MMc
Note I . Ranges 0-3 and 12-14 not standardized by I.T.U.
Note 2. Frequencies shall be expressed in kilocycles per second (kc/s) at and below 30,000 kilo-
cycles per second and in megacycles per second (Mc/s) above this frequency.
Note 3. Used as an adjective the word "Range" shall precede the number; thus: "Range 3."
SECTION 2
PROPERTIES OF MATERIALS
CONDUCTING MATERIALS
ABTt BY KNOX MCILWAIN PAGE
1. Definitions 02
2. Properties of Specific Conductors 03
3. Wire Tables 12
INSULATING MATERIALS
By W. R. DOHAN
4. Dielectric Properties 21
5. Solid Dielectric Materials 25
6. Liquid Dielectrics 48
7. Gases as Dielectrics 53
MAGNETIC MATERIALS
BY TL M. BOZORTH AND
R. A. CHEGWIDDEN
ART. PAGE
8. Magnetic Characteristics 57
9. High-permeability Materials 60
10. Permanent-magnet Materials 65
11. Magnetization Curve 68
12. Effect of Temperature 69
13. Stress and Magnetostriction 70
14. Effect of Frequency 70
15. Measurement of Magnetic Characteris-
tics 72
2-01
PROPERTIES OF MATERIALS
CONDUCTING MATERIALS
By Knox Mcllwain
Since all materials possess, to some extent, the ability to conduct electricity, whether
a particular material is called conducting or insulating is a matter only of _ relative degree.
In general, if a moderate potential difference, say from a voltaic cell, is placed across
a section of a material and a measurable current flows the substance is said to be con-
ducting, but if no conveniently detectable current flows it is considered insulating.
Among conducting materials are included pure metals, some metallic salts and oxides,
alloys, and the metalloids, carbon, silicon, and boron. Such substances as glass, dry paper
and silk, porcelain, and rubber possess such a very low conductivity that they are con-
sidered insulating materials.
1. DEFINITIONS
Conductivity. The conductivity of a material is the direct current conductance be-
tween the opposite, parallel faces of a portion of the material having unit length and un.it
cross-section.
Effective Conductivity. The effective conductivity of a material to a periodic current
is the effective conductance between the opposite, parallel faces of a portion of the mate-
rial having unit length and unit cross-section.
Resistivity. The resistivity of a material is the reciprocal of its conductivity.
Units of Resistivity. The resistivity may be expressed as the resistance of a 1-cm
cube of material; this unit is called the ohm per centimeter cube or preferably simply the
ohm-centimeter. In the English system the ohm-inch is used. When the material is to
be drawn into wires the ohm per mil-foot is used; this is the resistance of a wire 1 mil
(0.001 in.) in diameter and 1 ft long.
Units of Conductivity. The conductivity of a material 7 is numerically equal to the
reciprocal of its resistivity p and is expressed in mhos and megmhos per centimeter, etc.,
instead of ohm-centimeters and microhm-centimeters, etc., as used to express resistivity.
Thus y equals 1/p.
AnnealecL Copper Standard. The standard, or 100 per cent, conductivity is defined
'as follows:
1. At a temperature of 20 deg cent, the resistance of a wire of standard annealed copper
1 meter in length and of a uniform section of 1 sq mm is 1/53 ohm = 0.01724 ohm.
2. At a temperature of 20 deg cent, the density of standard annealed copper is 8.89
grams per cubic centimeter. This corresponds to 8.90 grams per cubic centimeter at
0 deg cent.
3. Thus, at 20 deg cent, the resistance of a wire of standard annealed copper of uniform
section, 1 meter in length and weighing 1 gram, is (1/55) X 8-89 = 0.15328 ohm.
Temperature Coefficient of Electric Resistance. The resistance temperature coeffi-
cient j8< of a substance at any temperature t is denned as the rate of change of resistance
at this temperature divided by the resistance Rt at this temperature:
The "mean" temperature coefficient at between any two temperatures t and ti "referred
to" the temperature * is defined as the "average" change in the resistance in this interval
per degree change of temperature, divided by the resistance at the lower temperature:
= Rg. - Rt
The temperature coefficients of 100 per cent conductivity copper are given in Table 1
2-02
PROPERTIES OF SPECIFIC CONDUCTORS
2-03
Table 1. Temperature Coefficients of Copper
Ohms per
Meter-gram
at 20° C
Per Cent
Conduc-
tivity
ao
ai5
CK20
0:25
«30
0. 16134
. 15966
.15802
.15753
.15640
.15482
.15328
95
96
97
97.3
98
99
100
0.00403
.00408
.00413
.00414
.00417
.00422
.00427
.00431
0.00380
.00385
.00389
.00390
.00393
.00397
.00401
.00405
0.00373
.00377
.00381
.00382
.00385
.00389
.00393
0.00367
.00370
,00374
.00375
.00378
.00382
.00385
.00389
0.00360
.00364
.00367
.00368
.00371
.00374
.00378
.00382
. 15176
101
.00397
The underlined values in the table have been adopted as standard by the American Institute of
Electrical Engineers.
2. PROPERTIES OF SPECIFIC CONDUCTORS
Conducting materials can be roughly divided into two groups: the good conductors,
and the resistive conductors. The good conductors are all metals, a group of some 50
chemical elements recognized as such by their hardness, ductility, malleability, luster,
and good conductivity of heat and electricity. Since these and other characteristics are
possessed by these elements in varying degrees there are some which are metallic in
some properties and non-metallic in others. Of these an electrically important group is
carbon, silicon, and boron, often called the metalloids, which are rather good conductors
of heat and electricity but have non-metallic mechanical properties. Almost all the
resistive conductors on the market today are solid solution alloys or those composed
largely of solid solutions. In electric circuits they are generally used either in devices
for purposes of operation, protection, or control, or as heating elements. It is usually
desirable for them to have properties of high resistivity and low temperature coefficient
of resistance, but in some cases a high temperature coefficient is useful — witness the use
of nickel as a filament control.
In general, the standard alloys for electrical resistance are made of nickel and chromium,
compositions of 80 per cent nickel and 20 per cent chromium having high resistance to
oxidation with maximum working temperatures up to about 1100 deg cent. By varying
the proportions of these and by the addition of different amounts of iron, copper, man-
ganese, zinc, and cobalt we are able to obtain alloys which have different resistivities,
temperature coefficients, melting points, magnetic properties, and heat- and corrosion-
resisting properties.
Tables 2 and 3 give the properties of materials available for the manufacture of con-
ductors and resistors; Table 4 gives the physical properties of some beryllium-copper alloys.
2-04
PROPERTIES OF MATERIALS
Table 2. Properties of Conducting Materials at Usual Temperatures
Description of Material
Resistivity
Microhm-cm
Temperature
Coefficient,
See Note a
Max.
Work-
ing
Temp.,
°C
Den-
sity,
jm
Tensile
Str.
(an-
nealed),
Ib
in.2
Coef.
Lin.
Expan-
sion
per °C
10~6X
0°C
20° C
Temp.,
°C
a
Acme * (Ni 30 + Cr 5 + Fe 65)
Advance * (Ni 45 + Cu 55)...
Alferon*(Cr 14.25 + A1 3.5 +
Fe8225)
(Similar Chr
(Similar Chr
(Similar
33.3
2.62
2.607
8.85
39.1
28.5
35
3.64
6.29
17.8
19.0
(800-
1,300)
4,000
2.6
(Similar Chr
(Similar
87.3
48.8
83.1
112
omel A)
omel C)
Comet)
2.828
(15°) 42
10.1
120
8 X 1012
7.60
4.59
110
100
108
112
99.5
omel A)
-Phenix)
20
20-100
20
20-500
0
0-100
18
15
20
0-160
(Simila
Sil
0-100
20
0-100
0-100
19-92
20
20
25-387
25-335
20-500
20-500
20-500
20-500
0.00072
.00002
.0006
.00016
.0012
.00423
.0039
.000897
.0036
.000387
r German
ver)
.0042
.00424
.004
.00204
.00158
.0005
.0038
.0036
.00025
(-.0006
-.0012)
-.0003
.00031
.00013
.00017
.00032
1,000
535
600
1,100
1,250
300
1,230
1,000
400
350
5,100
1,100
900
500
8.15
8.9
7.31
2.7
8.15
1.56
1.54
7.95
8.4
8.24
7.94
100,000
60,000
80,000
100,000
35,000
90,000
500
600
70,000
95,000
95,000
70,000
14.9
14
11.4
24
16
15.8
17
17
16
Alloy A
Alloy C
Alloy D
Alumel * (Ni 94 + Mn 2.5 +
Fe0.5 + A12 + Sil)
Aluminum (Pure)
Aluminum (Wire, 61% cond.).
Aluminum Bronze (Cu 97 +
A13)
Antimony
Argentan*(Cu61.6 + Nil5.8
+ Zn 22 6)
Argentan*(Cu56 + Ni26 +
Znl8)
Arsenic
Ascoloy*(Fe82-S6 + Crl6-
05)
Beryllium
Bismuth
Boron
Brass (Cu 90.9 + Zn 9.1)
Brass (Cu 65.8 + Zn 342) ....
Bronze (Cu 88 + Sn 12)
Cesium
Calcium (9937% pure)
Calido*(Ni59 + Crl6 + Fe
25)
Calorite * (Ni 65 + Cr 12 +
Fe 15 + Mn8).
Carbon (graphite)
Carbon (incandescent lamp) . .
Chromax * (Ni 30 + Cr 20 +
Fe 50) .
Chromel * A (Ni 80 + Cr 20)
Chromel *C (Ni 60 + Cr 16 +
Fe24)
Chromel *D(Ni 30 + Cr 20
+ Fe50)
Chronin * (Ni 83.7 + Cr 14.7}
Cimet * (Ni 25 + Fe 75) . . . .
range is given, the coefficient a is the mean value for the range, referred to the lower
* Trademark names.
PROPERTIES OF SPECIFIC CONDUCTORS
2-05
Table 2. Properties of Conducting Materials at Usual Temperatures — Continued
Description of Material
Resistivity
Microhm-cm
Temperature
Coefficient,
See Note a
Max.
Work-
ing
Temp.,
°C
Den-
sity,
Tensile
Str.
(an-
nealed),
Ib
in.2
Coef.
Liu.
Expan-
sion
per °C
10~6X
0°C
20° C
Temp.,
°C
a.
Climax* (Ni 25 + Fe 74 +
Mn 1)
(Similar
49.0
1.589
1.56
1.60
4.08
100
77
48
(Similar
(Similar
(Similar
(Similar
47
91.4
27.1
53
33.1
89,000
2.22
87
9.7
95
Advance)
49
48.8
1.7241
1.77
Lucero)
Comet)
Advance)
Invar)
83.2
8
133
92
49.2
28.2
33.8
(Similar
20
0-100
0
20-500
0-100
12
25
100
200
500
0-100
0-100
20
0-100
100
0-100
20
0-100
0-100
0
0
20
0
-50 to
100
20
20
20
20
18-100
20
Chromel
.0007
.00658
.0033
.00088
O.OOOOi
.000008
.000002
-.000033
-.000020
.000027
.00002
.00427
.00393
.00428
.0038
.00408
.00382
.00155
.00004
.000022
-.00003
.0011
.00005
±0.00002
.00016
.0000
.00207
.00031
.00368
.0034
C)
600
500
500
600
900
1,150
340
260
500
8.15
8.86
8.92
8.1
8.9
7.8
8.5
19.3
55,000
62,000
60,000
35,000
45,000
100,000
20,000
15
14.9
17
16.6
14
17.3
14.2
Cobalt (99 8% pure)
Comet * (Ni 30 + Cr 4.75 +
Fe 65 25)
Constaloy*(Ni45 + Cu55)..
Constantan * (Cu 60 + Ni 40)
Copel * (Ni 45 + Cu 55)
Copper (annealed standard) , . .
Copper (electrolytic) . .
Copper (hard-drawn)
Copper-iron (Fe 0 4%)
Copper-manganese (Cu 70 +
Mn 30)
Copper-manganese-iron (Cu
70.6 + Mn 23.2 + Fe 6.2)..
Copper-manganese-nickel (Cu
73 + Mn 24 + Ni 3)
Corronil * (Ni 70 + Cu 26 +
Mn4)
Cronin * D
Cronit * (Ni 60 + Cr 40)
Dilver * (similar Invar)
Dumet*(Ni46 + Fe54)....
Electris * (similar Phenix)
Elinvar* (Ni 36 + Cr 12 +
Fe 52) ....
Eureka * (similar Lucero)
Evanohm * (Cr 20 + Al 2.5 +
Cu 2 5 + Ni bal )
Excello* (Ni 85 + Cr 14 +
Fe0.5 + Mn0.5)
Excelsior * (similar Advance) . .
Ferro-nickel
Gallium
German silver fl 8% (Ni 18 +
Cu64 + Zn 18)
GerionfvniiiTfl , . » . , , ,
Gold (99.9%)
Glowray* (Ni 65 + Cr 12 +
Fe23)
NOTE a: Where a temperature range is given, the coefficient a is the mean value for the range, referred to the lower
temperature.
* Trademark names.
t German Silver-30% has substantially the same properties as "Advance."
2-06
PROPERTIES OF MATERIALS
Table 2. Properties of Conducting Materials at Usual Temperatures— Continued
Description of Material
Resistivity
Microhm-cm
Temperature
Coefficient,
See Note a
Max.
Work-
ing
Temp.,
°C
Den-
sity,
cm3
Tensile
Str.
(an-
nealed),
A
in.2
Coef.
Lin.
Expan-
sion
per °C
io-flx
0°C
20° C
Temp.,
°C
a.
Hipernik * (Ni 50 4- Fe 50) ...
Hopkinson alloy * (Ni 25 + Fe
75)
47.1
50.2
49
(Similar
8.37
(Similar-
6.10
8.85
11.8
45.7
74,4
97.8
85.0
19.8
63.3
8.55
4.35
5.0±
100
(Similar
20
47.1
50.2
91.61
Nirex)
Platinite)
10
135
103
94.6
22
10
48.2
4.6
14
48.2
20
Phenix)
20-100
20
20
0-100
20
0
0-100
0-100
100
20
10-35
10-35
0
20-500
20
20
0-100
20
0
20-100
20-250
20
0
0-100
20-100
15-35
25
100'
20-100
,0045
.000005
.000011
.0000±
.000005
.000479
0.0047
.00411
.00625
.0068
.0050
.00423
.00161
.0016
.00003
.00016
.000242
.00070
.00411
.0039
,0047
.00071
.0010
.004
.0038
.00004
.0045
.000015
.000000
—.000042
.0036
500
520
150
1,000
900
1,100
1,100
700
600
1,100
100
1,100
8.46
8.92
8.92
8.9
7.86
8.9
8.9
8.9
8.8
8.2
8.75
70,000
65,000
80,000
100,000
90,, 000
80,000
70,000
100,000
90,000
60,000
90,000
15
14
1.5
As glass
11.7
16
15
18
12.5
14.6
18.7
14.3
Hytemco*(Ni724-Fe28)..
la la* (Ni40H-Cu60soft)..
la la * (Ni 40 4- Cu 60 hard-
drawn) • • • •
Ideal * (Ni 40 4- Cu 58 4- Fe
1 4- Mn 1)
Inconel * (Or 13 4- Fe 8 4- Ni
49)
Indium
Invar * (Ni 36 4- Fe 64)
Invariant * (Ni 47 4- Fe 53) . .
Iridium
Iron (pure)
Iron (99.98% pure)
Iron (steel) soft , ...
Iron (steel) tempered glass hard
Iron, cast (soft)
Iron cast (hard)
KanthalD(Cr234-A134-
Co2 4- Fe bal.)
Karma * (Ni 80 4- Cr 20) . . . .
Kromax * (similar Karma) ....
Kromore * (Ni 85 + Or 15) . . .
Krupp metal (nickel steel)
Lead
Lead-bismuth (Pb 42.3 4- Bi
57,7)
Lohm * (Ni 6 4- Cu 94)
Lucero * (Ni 70 4- Cu 30) . . . .
Magno * (Ni 95 4- Mn 5)
Magnesium
Magnesium (free from zinc) . . .
Manganese-copper * (Cu 70 4-
Mn30)
Manganese-nickel (Mn 2 4- Ni
98)
Manganin* (Cu84-f-Mn 12
4-N14)
Magno*(Mn4.54-Ni95.5)..
temperItoeWhere * ^^^^ range is given' the coefficieilt « is ** *ean value for the range, referred to the lower
""Trademark names.
PROPERTIES OF SPECIFIC CONDUCTORS
2-07
Table 2. Properties of Conducting Materials at Usual Temperatures — Continued
Description of Material
Resistivity
Microhm-cm
Temperature
Coefficient,
See Note a
Max.
Work-
ing
Temp.,
°C
Den-
sity,
gm
cm3
Tensile
Str.
(an-
nealed),
Ib
m7
Coef.
Lin.
Expan-
sion
per°C
10~6X
0°C
20° C
Temp.,
°C
a
Marsh's patent * (Ni 75 + Or
25)
(Similar Chr
94.07
5.14
4.2
4.9
(Similar
40.8
6.93
9.9
29.4
10.21..
7.75
(Similar
45
9.83
omel A)
95.783
30
Lucero)
42.6
112
108
7.8
7.236
33.3
48.2
80.5
98.1
166
9.5
11
95.5
83.1
Premier)
34.4
(18°)
0-100
20
20-100
0-100
25
0-170
0-170
20
20-500
20-500
20
0-100
20
20
20
20-100
20-500
20-500
20
0
20
20
0
0
20
Noteb
.00089
.00018
.00435
.0033
.0050
.0050
.0020
.00017
0.00013
.006
.00618
.00400
.00027
.00020
.00135
.00012
.000066
.0033
.0035
.00018
.0011
.0040-
.003
.003
700
425
980
1,100
700
260
260
500
1,100
500
1,100
400
8.9
8.15
8.25
8.41
8.8
8.5
8.5
8.08
8.55
6.8
8,05
8.10
70,000
44,000
120,000
95,000
70,000
60,000
60,000
100,000
130,000
130,000
75,000
17.5
12.6
17
17
14,0
17.3
1.0
16.1
15.8
14
Mercury
Midohm * (Ni 23 + Cu 77) ..
Molybdenum (very pure)
Molybdenum (annealed)
Molybdenum (hard-drawn) . . .
Mond * No. 70 (Ni 70 + Cu
26 + Mn4)
Monel metal (Ni 67 + Cu 28
+ Mn5)
Nichrome*(Ni61 + CH5 +
Fe24)
Nichrome * V (Ni 80 + Cr 20)
Nickel
Nickel (electrolytic)
Nickel (very pure)
Nickel (commercial wire)
Nickel-chromium (Ni + Cr
and Fe + Mu)
Nickel-silver 18% (Ni 18 +
Cu64 + Zn 18)
Nickel-silver 30% (Ni 30 +
Cu 50 + Zn 20)
Nickel steel (4.35% Ni)
Nickelin * (same German sil-
ver)
Nicraloy * (similar Chromel) . .
Nilvar * (Ni 36 + Fe 64)
Nirex* (Cr 13 + Fe 8 + Ni
79)
Ohmax *
Osmium
Palladium
Palladium (very pure)
Peerless * (Ni 78.5 + Cr 16 +
Fe 3 + Mn 2)
Phenix * (Ni 25 + Fe 75)
Phosphor-bronze
Placet * (Ni 60 + Cr 15 + Fe
20 + Mn5)
Platinite * (Ni 42-46, Fe 58-
54)
Platinoid * (Cu 62 + Ni 15 +
Zn 22)
Platinum
NOTE a: Where a temperature range is given, the coefficient a is the mean value for the range, referred to the lower
temperature.
NOTE b: Use equation Rt = RQ (I + aT + 6T2) with a = 0.0008649 and 6 = 0.00000112.
* Trademark names.
2-08
PROPERTIES OF MATERIALS
Table 2. Properties of Conducting Materials at Usual Temperatures— Continued
Description of Material
Resistivity
Microhm-cm
Temperature
Coefficient,
See Note a
Max.
Work-
ing
Temp.,
°C
Den-
sity,
gm
Tensile
Str.
(an-
nealed),
Ib
in.2
Coef.
Lin.
Expan-
sion
per °C
10~6X
0°C
20° C
Temp.,
°C
a
cm3
Platinum, drawn, wire
10.96
31.6
21.14
6.1
(Similar
44.6
53
5.11
64.5
11.6
1.468
4.3
14.6
17.6
46.7
(Similar
10.5
(Similar Chr
(Similar Chr
(Similar Chr
103.0
133
95.7
Rayo)
25
113.0
58=b
1.629
(18°)
73
24.8
103.0
15.5
41
.2 X I06
(19.68)
46.7
Phenix)
11.5
melA)
melC)
melD)
5.51
0-100
0
-100 to
+ 100
0
15
0
20
20-500
20
0
0
0
0-94.3
0
20-250
20
20
0-100
0
20-500
20
0-100
20
20
20
0-100
20
18
.00367
.0037
.002±
.0008
.00143
.0057
.00036
.0001
.00018
.00041
0.0004
.0043
.0023
.0060
.0027
.000025
.0038
.00400
.0054
.00094
.00011
.0033
.0031
.000025
56X10~7
.00465
.0042
.0045
1,200
1,000
500
1,100
1,100
1,100
500
1,100
1,100
100
200
2,000
21.45
8.15
7.30
8.05
8.72
7.63
10.5
7.93
8.2
8.89
8.15
19.3
50,000
90,000
90,000
130,000
42,000
200,000
78,000
600,000
8.9
15.5
15
15.2
18.9
20
19.4
4
Platinum-indium (Pt 80 + Ir
20)
Platinum-rhodium (Pt 90 +
Rh 10)
Potassium
Premier * (Ni 61 + Cr 11 +
Fe 25 + Mn 3)
Radiohm*(Crl6.5 + AI5 +
Fe 78 5)
Rayo*(Ni85+Cr15)
Redray*(Ni85 + Crl5)....
Rheotan * (Ou 84 + Fe 12 +
Zn 4)
Rheotan * II (Cu 53.3 + Ni
25.3 + Fe4.5 + Znl6.9)...
Rhodium
Rose's metal * (Bi 48.9 + Sn
233 + Pb 27.6)
Rubidium
R-63 Alloy (Mn 4 + Si 1 +
Ni 95)
Silchrome * (Si + Cr + Fe) . . .
Silicon . .
Silver (99 78% pure)
Silver (electrolytic)
Sodium
Stainless Type 304 <Cr 18 +
Ni 8 -f Fe 74)
Steel (see iron)
Rfcrnntiufn . T -.--,- , , . . - , r
Superior * (Ni 78 + Cr 19.5 +
Fe 0.5 + Mn 2)
Tantalum
Tarnac * (similar Manganin) . .
Tellurium , t ,.,.,.
Thallium (pure)
Therlo * (Cu + Mn + Al) . . . .
Ticjo*(Ni 27.5 -hFe 72.5)....
Tin
Tophet*A
Tophet*C
Tophet * D
Tungsten
NOTE a: Where a temperature
temperature*
* Trademark names.
range is glven, the coefficient a is the mean value for the range, referred to the lower
PROPERTIES OF SPECIFIC CONDUCTORS
2-09
Table 2. Properties of Conducting Materials at Usual Temperatures — Continued
Description of Material
Resistivity
Microhm-cm
Temperature
Coefficient,
See Note a
Max.
Work-
ing
Temp.,
°C
Den-
sity,
gm
cm3
Tensile
Str.
' (an-
nealed),
Ib
ia.2
Coef.
Lin.
Expan-
sion
per°C
10~6X
0°C
20° C
Temp.,
°C
a
Tungsten (annealed)
51.8
5.38
5.75
(Similar
(Similar
(Similar
(Similar Eva
4.37
33.0
5.92
93.1
5.0
66.5
Advance)
45.7
43.2
Lohm)
15
90 Alloy)
8
87.2
nohm)
100
0-170
0-69.8
20
18-100
20
20-500
20-100
20-500
20-500
20-500
20-100
0-100
20
20-500
.0051
.0023
.000155
.00402
.00347
.0025
.0013
.0012
.0027
.0029
.00049
.0060
.00072
.00034
100
1,100
500
1,100
1,100
1,100
500
650
500
8.6
7.14
8.10
8.9
8.12
8.17
8.25
8.9
8.15
25,000
100,000
30.000
100,000
100,000
100,000
35,000
60,000
15.9
33
10.8
17.5
5.3
8.0
9.5
17.5
17.1
13.1
Wood's metal * (Bi 55.7 + Sn
13.7 +Pbl 3.7 + Cd 16.2).
Yankee silver * (similar Nickel
silver)
Zinc (pure)
Zinc (trace Fe)
14 Alloy (Ni 42 + Or 5.5 +
Fe52.5)
30 Alloy (Ni 2.25 + Cu 97.5).
42 Alloy (Ni 42 + Fe 58) ....
45 Alloy
46 Alloy (Ni 46 -h Fe 54)
52 Alloy (Ni 51 + Fe 49)
60 Alloy
90 Alloy (Ni 1 1 + Cu 89) . . . .
95 Alloy
99 Alloy (Ni 99.8)
193 Alloy (Ni 30 + Cr 2 +
Fe 67 + Mn 1 )
331 Alloy
525 Alloy
NOTE a: Where a temperature range is given, the coefficient a is the mean value for the range, referred to the lower
temperature.
* Trademark names.
2-10 PROPERTIES OF MATERIALS
Table 3. Properties of Conducting Materials at High Temperatures
Description of Material
Resistivity in Microhm centimeters
500° C
1000° C
1500° C
Al * (f d)
10
152
139.9
60X106 appx.
12.5
34.12
109
2700
3700
3300
2800
8. 5X1 OB appx.
4.8X106 appx.
0.22X106
5.1
2.50X106
5640X106
1570X106
94
330 XI 06 appx.
6.62
840
800
2.70X106
52 appx.
1260X106
115
10X106
102.85
0.418X106
0.824X106
81
2200X106
16.5
t
119
34.4
25.3
19.7X106
24
8X109
136
167.5
41
122
2400
3400
3000
2100
2.8X106
1.9X106
0.12X106
9.42
18X106
105
IX 106 appx,
12.54
860
650
1.7X106
1 1 1 appx.
31.4X106
4.8X106
125
98
1400X106
15.7X106
28.5
128
66
40.8
15X106 appx.
110X106
3.7X106
29
75X107
136
2200
2900
1600
0.85X106
24.8
37
890
580
1.2X106
131 appx.
166
3.4X106
148
40.5
0.5X106 appx.
98
52.6
o 5 vine
Brass (2 1 fused)
Brass (2 I solid)
Calido (solid)
Carbon (a)
Carbon (b)
Copper (solid} .
Copper chloride (fused) .
Copper oxide (Cu 0)
Copper oxide (Cu O«> powder),. ,,. ....
Ferro-nickel (solid) .
Glass
Gold (fused)
Gold (solid)
Graphite (a) ...
Graphite (b)
Iron (a) solid .
Iron (b) fused
Iron oxide (Fe^> Og, powder)
Krupp metal (solid)
Lead (fused)
Lead chloride (fused 520°)
Lead chloride (solid)
Lead-tin alloy (fused)
Magnesium oxide (powder)
Manganese oxide (powder)
Manganese oxide (Mn C>2» powder)
Molybdenum (solid)
KTArnst. filq.Tnpnf, IL
Nichrome* II (solid)
Platinum (a) solid
Platinum (b) solid
Porcelain
Quartz
Refrax*
* Trademark names.
PROPERTIES OF SPECIFIC CONDUCTORS
2-11
Table 3. Properties of Conducting Materials at High Temperatures — Continued
Description of Material
Resistivity in Microhm-centimeters
500° C
1000° C
1500° C
Silfrax* B
0.92X106
0.094X106
to 0. 023X106
120X106
5
0.547X106
36
54.62
18
18
36.60
0.84X106
3.5X106
17.01
0.90X106
57
68
30.5
33.4
26.7X106
0.7X106
23
78
74
80.5
43
50
Silver (fused)
Silver (solid)
Silver chloride (fused) . ..
Sodium chloride (fused) ... . . . »
Tantalum (solid)
Tantalum (a) solid , .
Tantalum (b) solid
Tin (fused)
Tungsten (solid)
Tungsten (a) solid
Tungsten (b) solid
Zinc oxide (powder)
* Trademark names.
Table 4.
Approximate Values for the Physical Properties of Beryllium-copper Alloys
of the 21 Per Cent Beryllium Class
Condition
Solution-
treated
"Annealed"
Solution-
treated and
Cold-worked
Solution-treated
and
Precipitation-
hardened
Solution-treated,
Cold-worked, and
Precipitation-
hardened
Electrical conductivity % I.A.-
C.S. at 20° C
17
17
(a) 20-25
(a) 20-25
Tensile strength, psi
70 , 000
90,000
(&) 32-38
(a) 160 000
(6) 32-38
(a) 180 000
Yield strength, psi, at 0.5%
elongation under load . .
(6) 130,000
(a) 150 000
(6) 140,000
(a) 175 000
Elongation in 2 in , %
35
(a) 3 0
(a) 2 0
Modulus of elasticity, psi . . .
16 X 106
18 4-19 4 X 106
Endurance limit, psi, at 108 re-
versals of stress
23,000
28,000
28,000
(a) Heat-treated for maximum hardness. (6) Heat-treated for maximum conductivity.
2-12
PROPERTIES OF MATERIALS
3. WIRE TABLES
Table 5. Solid Copper Wire
A. W. G. or B. & S. Gage; English Units
100 per cent conductivity; density 8.89 at 20 deg cent
Gage
No.
Diam-
eter in
Mils
Cross-section
Resistance at
20° C or 68° F
Weight in Pounds
Feet
per
Pound
Circular
Mils
Square
Inches
Ohms per
1000ft
Ohms
per Mile
per
1000ft
per
Mile
0000
460.0
211,600
0.1662
0.0490
0.25
640.5
3380
1.561
000
409.6
167,800
0. 1318
0.0618
0.32
507.9
2680
1.968
00
364.8
133,100
0.1045
0.0779
0.41
402.8
2130
2.482
0
324.9
105,500
0.08289
0.9082
0.51
319.5
1680
3.130
1
289.3
83,690
0.06573
0.1239
0.65
253.3
1340
3.947
2
257.6
66,370
0.05213
0.1563
0.82
200.9
1060
4.977
3
229.4
52,640
0.04134
0.1970
1.04
159.3
841
6.276
4
204.3
41,740
0.03278
0.2485
1.31
126.4
667
7.914
5
181.9
33,100
0.02600
0.3133
1.65
100.2
529
9.980
6
162.0
26,250
0.02062
0.3951
2.09
79.46
420
12.58
7
144.3
20,820
0.01635
0.4982
2.63
63.02
333
15.87
8
128.5
16,510
0.01297
0.6282
3.32
49.98
264
20.01
10
101.9
10,380
0.008155
0.9989
5.28
31.43
166
31.82
12
80.81
6,530
0.005129
1.588
8.38
19.77
104
50.59
14
64.08
4,107
0.003225
2.525
13.3
12.43
63.3
80.44
15
57.07
3,257
0.002558
3.184
16.8
9.858
52.0
101.4
16
50.82
2,583
0.002028
4.015
21.2
7.818
41.3
127.9
17
45.26
2,048
0.001609
5.064
26.7
6.200
32.7
161.3
18
40.30
1,624
0.001276
6.385
33.7
4.917
26.0
203.4
19
35.89
1,288
0.001012
8.051
42.5
3.899
20.6
256.5
20
31.96
1,022
0.0008023
10.15
53.6
3.092
16.3
323.4
21
28.46
810.1
0.0006363
12.80
67.6
2.452
12.9
407.8
22
25.35
642.4
0.0005046
16.14
85.2
1.945
10.3
514.2
23
22.57
509.5
0.0004002
20.36
108
1.542
8.14
648.4
24
20.10
404.0
0.0003173
25.67
135
1.223
6.46
817.7
25
17.90
320.4
0.0002517
32.37
171
0.9699
5.12
1,031
26
15.94
254.1
0.0061996
40.82
216
0.7692
4.06
1,300
27
14.20
201.5
0.0001583
51.46
272
0.6100
3.22
1,639
28
12.64
159.8
0.0001255
64.90
343
0.4837
2.55
2,067
29
11.26
126.7
0.00009953
81.84
432
0.3836
2.03
2,607
30
10.03
100.5
0.00007894
103.2
545
0.3042
1.61
3,287
31
8.928
79.70
0,00006260
130.1
687
0.2413
1.27
4,145
32
7.950
63.21
0.00004964
164.1
866
0.1913
1.01
5,227
33
7.080
50.13
0.00003937
206.9
1,090
0.1517
0.814
6,591
34
6.305
39.75
0.00003122
260.9
1,380
0. 1203
0.635
8,310
35
5.615
31.52
0.00002476
329.0
1,740
0.09542
0.504
10,480
36
5.000
25.00
0.00001964
414.8
2,190
0.07568
0.400
13,210
37
4.453
19.83
0.00001557
523.1
2,762
0.06001
0.317
16,660
38
3.965
15.72
0.00001235
659.6
3,480
0.04759
0.251
21,010
39
3.531
12.47
0.000009793
831.8
4,392
0.03774
0.199
26,500
40
3.145
9.888
0.000007766
049
5,540
0.02993
0.158
33,410
41
2.800
7.842
0.000006159
323
6,983
0.02374
0.125
42,130
42
2.494
6.219
0.000004884
668
8,806
0.01882
0.0994
53,120
43
44
2.221
1.978
4.932
3.911
0.000003873
0.000003072
2103
2652
11,100
14,000
0.01493
0.01184
0.. 0788
0 0625
66,990
84,470
WIRE TABLES
2-13
Table 6. Solid Copper Wire
A. W. G. or B. & S. Gage in Metric Units
100 per cent conductivity; density 8.89 at 20 deg cent
Gage No.
Diameter,
mm
Cross-section,
sq mm
Ohms per Kilometer
20° C
Kilograms per
Kilometer
0000
000
00
11.68
10.40
9.266
107.2
85.03
67.43
0.1608
0.2028
0.2557
953.2
755.9
599.5
0
2
8.252
7.348
6.544
53.48
42.41
33.63
0.3224
0.4066
0.5126
475.4
377.0
299.0
3
4
5
5.827
5. 189
4.621
26.67
21.15
16.77
0.6464
0.8152
1.028
237.1
188.0
149.1
6
7
8
4.115
3.665
3.264
13.30
10.55
8.366
1.296
1.634
2.061
118.2
93.78
74.37
10
12
14
2.588
2.053
1.628
5.261
3.309
2.081
3.277
5.211
8.285
46.77
29.42
18.50
15
16
17
1.450
1.291
1.150
1.650
1.309
1.038
10.45
13.18
16.61
14.67
11.63
9.226
18
19
20
1.024
0.9116
0.8118
0.8231
0.6527
0.5176
20.95
26.42
33.31
7.317
5.803
4.602
21
22
23
0.7230
0.6438
0.5733
0.4105
0.3255
0.2582
42.00
52.96
66.79
3.649
2.894
2.295
24
25
26
0.5106
0.4547
0.4049
0.2047
0.1624
0.1288
84.22
106.2
133.9
1.820
1.443
1.145
27
28
29
0.3606
0.3211
0.2859
0.1021
0.08098
0.06422
168.8
212.9
268.5
0.9078
0.7199
0.5709
30
31
32
0.2546
0.2268
0.2019
0.05093
0.04039
0.03203
338.6
426.9
538.3
0.4527
0.3590
0.2847
33
34
35
0.1798
0.1601
0.1426
0.02540
0.02014
0.01597
678.8
856.0
1079
0.2258
0.1791
0.1420
36
37
38
0.1270
0.1131
0.1007
0.01267
0.01005
0.007967
1361
1716
2164
0.1126
0.08931
0.07083
39
40
41
0.08969
0.07987
0.07113
0.006318
0.005010
0.003973
2729
3441
4339
0.05617
0.04454
0.03532
42
43
44
0.06334
0.05641
0.05023
0.003151
0.002499
0.001982
5472
6900
8700
0.02801
0.02222
0.01762
2-14
PROPERTIES OF MATERIALS
Table 7. Solid Copper Wire
British Standard Wire Gage; English Units
100 per cent conductivity; density 8.89 at 20 deg cent
Gage No.
Diameter,
mils
Cross-section
Ohms per
1000ft,
15.6° C or
60° F*
Pounds per
1000 ft
Circular Mils
Square Inches
7-0
500
250,000
0.1964
0.04077
756.8
6-0
464
215,300
0.1691
0.04734
651.7
5-0
432
186,600
0.1466
0.05461
564.9
4-0
400
160,000
0.1257
0.06370
484.3
3-0
372
138,400
0. 1087
0.07365
418.9
2-0
348
121,100
0.09512
0.08416
366.6
0
324
105,000
0.08245
0.09709
317.8
1
300
90,000
0,07069
0.1132
272.4
2
276
76,180
0.05983
0.1338
230.6
3
252
63,500
0.04988
0.1605
192.2
4
232
53,820
0.04227
0.1894
162.9
5
212
44,940
0.03530
0.2268
136.0
6
192
36,860
0.02895
0.2765
111.6
7
176
30,980
0.02433
0.3290
93.76
8
160
25,600
0.02011
0.3981
77.49
9
144
20,740
0.01629
0.4915
62.77
10
128
16,380
0.01287
0.6221
49.59
11
116
13,460
0.01057
0.7574
40.73
12
104
10,820
0.008495
0.9423
32.74
13
92
8,464
0.006648
1.204
25.62
14
80
6,400
0.005027
1.592
19.37
15
72
5,184
0.004072
1.966
15.69
16
64
4,096
0.003217
2.488
12.40
17
56
3,136
0.002463
3.250
9.493
18
48
2,304
0.001810
4.424
6.974
19
40
1,600
0.001257
6.370
4.843
20
36
1,296
0.001018
7.864
3.923
22
28
784.0
0.0006158
13.00
2.373
24
22
484.0
0.0003801
21.06
1.465
26
18
324.0
0.0002545
31.46
0.9807
28
14.8
219.0
0.0001720
46.54
0.6630
30
12.4
153.8
0.0001208
66.28
0 4654
32
10.8
116.6
0.00009161
87.38
0.3531
34
9.2
84.64
0.00006648
120.4
0.2562
36
7.6
57.76
0.00004536
176.5
0. 1748
38
6.0
36.00
0.00002827
283.1
OJ090
40
4.8
23.04
0.00001810
442.4
0.06974
42
4.0
16.00
0.00001257
637.0
0.04843
44
3.2
10.24
0.000008042
995.3
0.03100
46
2.4
5.760
0.000004524
1,769
0.01744
48
1.6
2.560
0.000002011
3,981
0,007749
50
1.0
1.000
0.0000007854
10,190
0,003027
e i. * £et ^"LF^ £ent conductivity, B6o - resistance of 100 per cent conductivity w
Eahr (from table), Rt — resistance of wire of conductivity C at any temperature t deg
Rt - ~ RQQ [I + 0.00223ft - 60)]
ire at 60 deg
fahr; then
WIRE TABLES
2-15
Table 8. Solid Copper Wire
" Millimeter Gage"; Metric Units and Circular Mile
100 per cent conductivity; density 8.89 at 20 deg cent
Diameter,
mm
Cross-section,
sq mm
Ohms per Kilo-
meter, 20° C
Kilograms per
Kilometer
Cross-section,
cir rn.lls *
10.0
9.0
8.0
7.0
6.0
5.0
4.5
4.0
3.5
3.0
2.5
2.0 -
1.8
1.6
1.4
1.2
1.0
0.90
78.54
63.62
50.27
38.48
28.27
19.64
15.90
12.57
9.621
7.069
4.909
3.142
2.545
2.011
1.539
1.131
0.7854
0.6362
0.2195
0.2710
0.3430
0.4480
0.6098
0.8781
1.084
1.372
1.792
2.439
3.512
5.488
6.775
8.575
11.20
15.24
21.95
27.10
698.2
565.6
446.9
342.1
251.4
174.6
141.4
111.7
85.53
62.84
43.64
27.93
22.62
17.87
13.69
10.05
6.982
5.656
155,000
125,550
99,200
75,950
55,800
38,750
31,380
24,800
18,990
13,950
9,690
6,200
5,010
3,970
3,040
2,230
1,550
0.80
0.5027
34.30
4.469
0.70
0.3848
44.80
3.421
0.60
0.2827
60.98
2.514
0 50
0 1964
87 81
1 746
0 45
0. 1590
108.4
1 414
0.40
0.1257
137.2
1.117
0 35
0 09621
179 2
0.8553
0 30
0 07069
243.9
0 6284
0.25
0.04909
351.2
0.4364
0.20
0.03142
548.8
0.2793
0 15
0.01767
975.6
0. 1571
0 10
0 007854
2195
0.06982
0.05
0.001964
8781
0.01746
* One square millimeter equals 1973.52 circular mile.
2-16 PROPERTIES OF MATERIALS
Table 9. Solid Copper Wire; Ohms per Unit Weight
A. W. G. or B. & S. Gage; English and Metric Units
100 per cent conductivity ; density 8.89 at 20 deg cent
Gage
No.
Ohms per Pound
Ohms per Kilogram
0° C
32° F
20° C
68° F
50° C
122°F
0°C
20° C
50° C
0000
0.0000705!
0.00007652
0.00008554
0.0001554
0.0001687
0.0001886
000
0.0001121
0.0001217
0.0001360
0.0002472
0.0002682
0.0002999
00
0,0001783
0.0001935
0.0002163
0.0003930
0.0004265
0.0004768
0
0.0002835
0.0003076
0.0003439
0.0006249
0.0006782
0.0007582
1
0.0004507
0.0004891
0.0005468
0.0009936
0.001078
0.001206
2
0.0007166
0.0007778
0.0008695
0.001580
0.001715
0.001917
3
0.001140
0.001237
0.001383
0.002512
0.002726
0.003048
4
0.001812
0.001966
0.002198
0.003995
0.004335
0.004846
5
0.002881
0.003127
0.003495
0.006352
0.006893
0.007706
6
0.004581
0.004972
0.005558
.0.01010
0.01096
0.01225
7
0.007284
0.007906
0.008838
0.01606
0.01743
0.01948
8
0.01158
0.01257
0.01405
0.02553
0.02771
0.03098
9
0.01842
0.01999
0.02234
0.04060
0.04407
0.04926
10
0.02928
0.03178
0.03553
0.06456
0.07006
0.07833
11
0.04656
0.05053
0.05649
0.1026
0.1114
0.1245
12
0.07404
0.08035
0.08983
0.1632
0.1771
0. 1980
13
0.1177
0.1278
0.1428
0.2595
0.2817
0.3149
14
0.1872
0.2032
0.2271
0.4127
0.4479
0.5007
15
0.2976
0.3230
0.3611
0.6562
0.7121
0.7961
16
0.4733
0.5136
0.5742
1.043
1.132
1.266
17
0.7525
0.8167
0.9130
1.659
1.800
2.013
18
1.197
1.299
1.452
2.638
2.863
3.201
19
1.903
2.065
2.308
4.194
4.552
5.089
20
3,025
3.283
3.670
6.670
7.238
8.092
21
4.810
5.221
5.836
10.60
11.51
12.87
22
7.649
8.302
9.280
16.86
18.30
20.46
23
12.16
13.20
14.76
26.81
29.10
32.53
24
19.34
20.99
23.46
42.63
46.27
51.73
25
30.75
33.37
37.31
67.79
73.57
82.25
26
48.89
53.06
59.32
107.8
117.0
131.8
27
77.74
84.37
94.32
171.4
186.0
207 9
28
123.6
134.2
150.0
272.5
295.8
330.6
29
196.6
213.3
238.5
433.3
470.3
525.7
30
312.5
339.2
379.2
689.0
747.8
836.0
31
497.0
539.3
602.9
1,096
1,189
1,329
32
790.2
857.6
958.7
1,742
1,891
2,114
33
1,256
1,364
1,524
2,770
3,006
3,361
34
1,998
2,168
2,424
4,404
4,780
5,344
35
3,177
3,448
3,854
7,003
7,601
8,497
36
37
38
5,051
8,032
12,770
5,482
8,717
13,860
6,128
9,744
15,490
11,140
17,710
28,150
12,080
19,220
30,560
13,510
21,480
34,160
39
40
41
20,310
32,290
51,340
22,040
35,040
55,720
24,640
39,170
62,290
44,770
71,180
113,200
48,590
77,260
122,800
54,310
86,360
137,300
42
43
44
81,640
129,800
206,400
88,600
140,900
224,000
99,050
157,500
250,400
180,000
286,200
455,000
195,300
310,600
493,900
218,400
347,200
552,100
WIRE TABLES
2-17
Table 10. Solid Aluminum Wire
A. W. G. or B. & S. Gage; English Units
61 per cent conductivity; density 2.70
Gage
No.
Diam-
eter,
mils
Cross-section
Resistance at
20° C or 68° F *
Weight in Pounds
Feet per
Pound
Circular
Mils
Square
Inches
Ohms per
1000ft
Ohms per
Mile
per
1000 ft
per
Mile
0000
460.0
211,600
0.1662
0.0804
0.424
195
1027
5.14
000
409.6
167,800
0.1318
0.101
0.535
154
815
6.48
00
364.8
153,100
0.1045
0.128
0.675
122
646
8.17
0
324.9
105,500
0.08289
0.161
0.851
97.0
512
10.31
1
289.3
83,690
0.06573
0.203
1.073
76.9
406
13.00
2
257.6
66,370
0.05213
0.256
1.353
61.0
322
16.39
3
229.4
52,630
0.04134
0.323
1.706
48.4
255
20.7
4
204.3
41,740
0.03278
0.408
2.15
38.4
203
26.1
5
181.9
33,100
0.02600
0.514
2.71
30.4
160.7
32.9
6
162.0
26,250
0.02062
0.648
3.42
24.1
127.4
41.4
7
144.3
20,820
0.01635
0.817
4.31
19.1
101.0
52.3
8
128.5
16,510
0.01297
1.03
5.44
15.2
80.2
65.9
10
101.9
10,380
0.008155
1.64
8.65
9.55
50.4
104.8
12
80.81
6,530
0.005129
2.61
13.76
6.00
31.7
166.6
14
64.08
4,107
0.003225
4.14
21.9
3.78
19.93
265
15
57.07
3,257
0.002558
5.22
27.6
2.99
15.81
334
16
50.82
2,583
0.002029
6.59
34.8
2.37
12.54
421
17
45.26
2,048
0.001609
8.31
43.8
1.88
9.94
531
18
40.30
1,624
0.001276
10.5
55.3
1.49
7.89
670
19
35.89
1,288
0.001012
13.2
69.7
1.18
6.25
844
20
31.96
1,022
0.0008023
16.7
87.9
0.939
4.96
1,065
21
28.46
810.1
0.0006363
21.0
110.9
0.745
3.93
1,343
22
25.35
642.4
0.0005046
26.5
139.8
0.591
3.12
1,693
23
22.57
509.5
0.0004002
33.4
176.3
0.468
2.47
2,130
24
20.10
404.0
0.0003173
42.1
222
0.371
1.961
2,690
25
17.90
320.4
0.0002517
53.1
280
0.295
1.556
3,390
26
15.94
254.1
0.0001996
67.0
353
0.234
1.233
4,280
27
14.20
201.5
0.0001583
84.4
446
0.185
0.978
5,400
28
12.64
159.8
0.0001255
106
562
0.147
0.776
6,810
29
11.26
126.7
0.00009953
134
709
0.117
0.615
8,580
30
10.03
100.5
0.00007894
169
894
0.0924
0.488
10,820
31
8.928
79.70
0.00006260
213
1127
0.0733
0.387
13,650
32
7.950
63.21
0.00004964
269
1421
0.0581
0.307
17,210
33
7.080
50.13
0.00003937
339
1792
0.0461
0.243
21,700 '
34
6.305
39.75
0.00003122
428
2260
0.0365
0.1929
27,400
35
5.615
31.52
0.00002476
540
2850
0.0290
0. 1530
34,510
* Let C =» per cent conductivity,
cent (from table) , Rt = resistance ol
fir
20 = resistance of 61 per cent conductivity wire at 20 deg
= resistance of wire of conductivity C at any temperature t deg cent; then
61 #20 r
C
5 [1 + 0.004« - 20)1
2-18
PROPERTIES OF MATERIALS
Table 11. Solid Aluminum Wire
A. W. G. or B. & S. Gage in Metric Units
61 per cent conductivity; density 2.70; temperature 20 deg cent or 68 deg fahr *
Gage No.
Diameter,
mm
Cross-section,
Ohms per
Kilometer
Kilograms per
Kilometer
0000
11.68
107.2
0.264
289
000
10.40
85.03
0.333
230
00
9.266
67.43
0.419
182
0
8.252
53.48
0.529
144
1
7.348
42.41
0.667
114
2
6.544
33.63
0.841
90.8
3
5.827
26.67
1.06
72.0
4
5.189
21.15
T.34
57.1
5
4.621
16.77
T.69
45.3
6
4.115
13.30
2.13
35.9
7
3.665
10.55
2.68
28.5
8
3.264
8.366
3.38
22.6
10
2.588
5.261
5.38
H.2
12
2.053
3.309
8.55
8.93
14
1.628
2.081
13.6
5.62
15
1.450
1.650
17.1
4.46
16
1.291
1.309
21.6
3.53
17
1.150
1.038
27.3
2.80
18
1.024
0.8231
34.4
2.22
19
0.9116
0.6527
43.3
1.76
20
0.8118
0.5176
54.6
1.40
21
0.7230
0.4105
68.9
T.IT
22
0.6438
0.3255
86.9
0.879
23
0.5733
0.2582
110
0.697
24
0.5106
0.2047
738
0.553
25
0.4547
0.1624
174
0.438
26
0.4049
0.1288
220
0.348
27
0.3606
0.1021
277
0.276
28
0.3211
0.08098
349
0 219
29
0.2859
0.06422
440
0.173
30
31
32
0.2546
0.2268
0.2019
0.05093
0.04039
0.03203
555
700
883
0.138
0.109
0.0865
33
34
35
0.1798
0.1601
0.1426
0.02540
0.02014
0.01597
1110
1400
1770
0.0686
0.0544
0.0431
cent
- resistance of 61
wire of conductivity C
per cent conductivity wire at 20 dee
at any tempeiature t deg ; cent; the?
- 20)]
The temperature coefficient is approzimate only.
WIRE TABLES
2-19
Table 12. Solid Steel Wire
American Steel Wire Gage; English Units
12.5 per cent conductivity; density 7.78
Am.
Steel
Wire
Gage
No.
Diameter
Cross-section
Resistance at
20° C or 68° F *
Weight in
Pounds
Feet
per
Pound
In.
Mils
Circular
Mils
Square
Inches
Ohms per
1000ft
Ohms per
Mile
per
1000ft
per
Mile
1/2
500.0
250,000
0.1964
0.332
1.752
662.5
3499
.51
7-0
490.0
240,100
0.1886
0.346
1.825
636.3
3360
.53
15/32
468.8
219,800
0.1726
0.378
1.993
582.4
3075
.72
6-0
460.0
211,600
0.1662
0.392
2.07
560.8
2961
.78
Vl6
437.5
191,400
0.1503
0.433
2.29
507.2
2678
.97
5-0
430.0
184,900
0.1452
0.449
2.37
490.0
2587
2.04
13/32
406.3
165,000
0.1296
0.503
2.65
436.8
2306
2.28
4-0
393.8
155,100
0.1218
0.535
2.82
411.9
2175
2.42
3/8
375.0
140,600
0.1104
0.590
3.12
372.6
1967
2.68
3-0
362.5
131,400
0.1032
0.631
3.33
348.2
1839
2.87
H/32
343.8
118,200
0.09280
0.702
3.71
313.1
1653
3.19
2-0
331.0
109,600
0.08605
0.757
4.00
290.3
1533
3.44
5/16
312.5
97,660
0.07670
0.850
4.49
258.8
1366
3.86
0
306.5
93,940
0.07378
0.883
4.66
249.0
1315
4.02
1
283.0
80,090
0.06290
1.036
5.47
212.2
1121
4.71
9/32
281.3
79,100
0.06213
.049
5.54
209.6
1107
4.77
2
262.5
68,910
0.05412
.204
6.36
182.6
964.1
5.48
V4
250.0
62,500
0.04909
.328
7.01
165.6
874.5
6.04
3
243.7
59,490
0.04665
.397
7.38
157.4
831.0
6.35
4
225.3
50,760
0.03987
.635
8.63
134.5
710.2
7.43
7/32
218.8
47,850
0.03758
.734
9.15
126.8
669.5
7.89
5
207.0
42,850
0.03365
1.936
10.22
113.6
599.5
8.81
6
192.0
36,860
0.02895
2.25
11.88
97.7
515.8
10.23
3/16
187.5
35,160
0.02761
2.36
12.46
93.2
491.9
10.73
7
177.0
31,330
0.02461
2.65
13.98
83.0
438.4
12.04
8
162.0
26,240
0.02061
3.16
16.69
69.6
367.2
14.38
5/32
156.3
24,410
0.01917
3.40
17.95
64.7
341.6
15.46
9
148.3
21,990
0.01727
3.77
19.92
58.3
307.8
17.16
10
135.0
18,200
0.01431
4.55
24.0
48.3
255.0
20.70
V8
125.0
15,630
0.01227
5.31
28.0
41.4
218.6
24.15
11
120.5
14,520
0.01140
5.71
30.2
38.5
203.2
25.98
12
105.5
11,130
0.00874
7.45
39.4
29.5
155.7
33.90
3/32
93.8
8,789
0.00690
9.44
49.8
23.3
123.0
42.94
13
91.5
8,372
0.00658
9.91
52.3
22.1
117.2
45.16
14
80.0
6,400
0.00503
12.96
68.5
17.0
89.55
58.97
15
72.0
5,184
0.00407
16.01
84.5
13.7
72.53
72.80
16
62.5
3,906
0.00307
21.2
112.1
10.4
54.66
96.60
1/16
62.5
3,906
0.00307
21.2
112.1
10.4
54.66
96.60
17
54.0
2,916
0.00229
28.5
150.2
7.73
40.80
129.5
18
47.5
2,256
0.00177
36.8
194.2
5.98
31.57
167.2
19
41.0
1,681
0.00132
49.4
261
4.45
23.52
224.4
20
34.8
1,211
0.00095
68.5
362
3.21
16.95
311.5
21
31.8
1,008
0.00079
82.3
435
2.67
14.11
374.4
1/32
31.3
977
0.00076
85.0
449
2.59
13.66
386.5
22
28.6
818
0.00064
101.4
536
2.17
11.45
461.1
23
25.8
666
0.00052
124.6
658
1.76
9.31
567.0
24
23.0
529
0.00042
156.8
828
1.40
7.40
713.5
25
20.4
416
0.00033
199.4
1053
1.10
5.82
907.0
* Let C ~ per cent conductivity,
#20 = resistance of 12.5 per cent conductivity wire at 20 deg cent (from table),
Rt — resistance of wire of conductivity C at any temperature t deg cent; then
Rt „ 12-*20 [1 + 0.006(* - 20)]
The temperature coefficient is approximate only.
2-20
PROPERTIES OF MATERIALS
Table 12. Solid Steel Wire— Continued
American Steel Wire Gage; English Units
12.5 per cent conductivity; density 7.78
Am.
Steel
Diameter
Cross-section
Resistance at
20° C or 68° F *
Weight in
Pounds
Feet
per
Wire
Gage
No.
In.
Mils
Circular
Mils
Square
Inches
Ohms per
1000 ft
Ohms per
Mile
per
1000 ft
per
Mile
Pound
26
18.1
328
0.00026
253
1337
0.87
4.58
1152
27
17 3
299
0.00024
277
1464
0.79
4.19
1261
28
16.2
262
0.00021
316
1669
0.70
3.67
1438
29
15.0
225
0.00018
469
1947
0.60
3.15
1677
30
14 0
196
0.00015
424
2240
0.52
2.74
1925
31
13.2
174
0.00014
476
2510
0.46
2.44
2166
32
12.8
164
0.00013
506
2670
0.43
2.30
2303
33
11.8
139
0.00011
596
3150
0.37
1.95
2710
34
10.4
108
0.00008
767
4050
0.29
1.51
3489
35
9.5
90
0.00007
919
4850
0.24
1.26
4193
36
9.0
81
0 00006
1023
5410
0.21
1.13]
4659
* Let C «* per cent conductivity,
£20 = resistance of 12.5 per cent conductivity wire at 20 deg cent (from _ table),
Rt =» resistance of wire of conductivity C at any temperature t deg cent; then
Rt = is-yfro u + Oj006(< _ 20)]
The temperature coefficient is approximate only.
COPPER-CLAD STEEL WIRE. This wire consists of a steel core and a concentric
coat of copper permanently welded thereto. It is used chiefly for long-span transmission
and telephone wire. It is made in several grades, which differ in the relative amounts of
steel and copper. The grades are designated by the corresponding conductivity expressed
as percentages of the Annealed Copper Standard: e. g., 40 per cent grade has a conductivity
of 40 per cent.
Table 13. Copper-clad Steel Wire
A. W, G. or B. & S. Gage; English Units
40 per cent conductivity; density 8.26
Gage
No.
Diam-
eter,
mils
Cross-section
Resistance at
23.9° C or 75° F *
Weight in
Pounds
Feet
per
Pound
Circular
Mils
Square
Inches
Ohms per
1000ft
Ohms per
Mile
per
1000ft
per
Mile
0000
460.0
211,600
0. 1662
0.123
0.649
595
3140
1.68
000
409.6
167,800
0.1318
0.154
0.813
471
2490
2.12
00
364.8
133,100
0.1045
0.195
1.03
374
1970
2.67
0
324.9
105,500
0.08289
0.246
1.30
297
1570
3.37
1
289.3
83,690
0.06573
0.310
1.64
235
1240
4.26
2
257.6
66,370
0.05213
0.390
2.06
186
982
5.38
3
229.4
52,630
0.04134
0.492
2.60
148
781
6.76
4
204.3
41,740
0.03278
0.622
3.28
117
618
8.55
5
181.9
33,100
0.02600
0.782
4.13
92.9
491
10.76
6
162.0
26,250
0.02062
0.987
5.21
73.7
389
13.57
7
144.3
20,820
0.01635
1.25
6.60
58.5
309
17.09
8
128.5
16,510
0.01297
1.57
8.29
46.4
245
21.6
9
114.4
13,090
0.01028
1.98
10.5
36.8
194
27.2
10
101.9
10,380
0.008155
2.50
13.2
29.2
154
34.2
11
90.74
8,234
0.006467
3.15
16.6
23.1
122
43.3
12
80.81
6,530
0.005129
3.97
21.0
18.3
96.6
54.6
13
71.96
5,178
0.004067
5.00
26.4
14.6
77.1
68.5
14
64.08
4,107
0.003225
6.31
33.3
11.5
60.7
87.0
* Let (7 » per cent conductivity,
-Kw. 9 *= resistance of 40 per cent conductivity wire at 23.9 deg cent (from table),
Rt = resistance of mre of conductivity C at temperature t deg cent; then.
Rt = 40 ^23-9 [1 + 0.00432(4 - 23.9)]
c
The temperature coefficient ia approximate only.
DIELECTRIC PROPERTIES
2-21
ALLOY WIRES OF HIGH TENSILE STRENGTH. Copper alloys having a low con-
ductivity but a tensile strength from 50 to 100 per cent greater than that of copper are
sometimes used where strength or hardness is a primary requisite, as in long spans of
small wires or for trolley wires.
TENSILE BREAKING LOAD. The tensile strength in pounds for solid wires from
1/16 to 1/2 in. in diameter is given in Table 14.
Table 14. Breaking Load for Solid Wires in Pounds per Wire
Gage No.
A.W.G.
or B. & S.
Diameter
Hard-drawn
Copper
(A.S.T.M.) *
Hard-drawn
Aluminum
(23,000 to
33,300 ib
per sq in.)
Copper-clad
Steel,
40 per cent
Grade
Steel
(100,0001b
per sq in.) f
In.
Mils
V2
500
9310
4520
11,400
19,640
0000
460
8140
3820
10,000
16,620
Vl6
437
7500
3460
9,250
15,030
000
410
6720
3030
8,300
13,180
3/8
375
5800
2540
7,150
11,040
00
365
5540
2400
6,850
10,450
0
325
4520
1910
5,700
8,289
5/16
312
4220
1770
5,400
7,670
1
289
3680
1530
4,800
6,573
2
258
3000
1240
4,000
5,213
V4
250
2830
1170
3,780
4,909
3
229
2420
1000
3,200
4,134
4
204
1950
810
2,600
3,278
3/16
187
1680
693
2,300
2,761
5
182
1570
655
2,200
2,600
6
162
1270
532
1,800
2,062
7
144
1020
432
1,450
1,635
8
129
822
351
1,200
1,297
Vs
125
780
335
1,150
1,227
9
114
660
287
975
1,028
10
102
528
234
800
816
11
91
423
191
650
647
12
81
337
155
510
513
13
72
268
126
410
407
14
64
213
103
330
323
Vl6
62
203
98
310
307
* Tensile strength in pounds per square inch ranging from 49,000 for No. 0000 to 66,200 for
No. 14; see below.
t For wires having a tensile strength of S pounds per square inch, multiply by 5/100,000. The
tensile strength of steel varies from 60,000 to 225,000 Ib per sq in.
INSULATING MATERIALS
By W. R. Dohan
4. DIELECTRIC PROPERTIES
Dielectric Constant. The dielectric constant, K, of an insulating material is the ratio of
the capacitance of an electrode system using the material as a dielectric to its capacitance
with a vacuum dielectric. When the material has appreciable losses so that the parallel
capacitance, Cp (determined by comparison with a standard capacitor and a parallel con-
ductance, <2), differs significantly from the effective series capacitance Ca (determined by
comparison with a standard capacitor and a series resistance, R), it is standard to use
the value of Cp in computing the dielectric constant. These capacitances are related by
the following formula:
where 8 = the loss angle or phase difference.
D — the dissipation factor.
2-22 PROPERTIES OF MATERIALS
Since the dielectric constant may vary considerably with frequency or temperature the
conditions of measurement should always be stated.
Phase Difference or Loss Angle. The difference between the theoretical 90 electrical
degrees phase advance of the current through a perfect capacitor and the actual angle of
phase advance, 6, of the current through the dielectric material is known as the phase
difference, or loss angle, 5.
Dissipation Factor. For convenience in reference and calculation the tangent oi^the
loss angle, 5, has been assigned the standard designation "dissipation factor" and given
the symbol D.
Power Factor. The power factor of a dielectric material is the ratio of the power loss
in the material to the product of the applied voltage and current. The power factor there-
fore is equal to the cosine of the angle of phase advance, 0, and to the sine of the comple-
mentary angle, 5. The sine and tangent of a small loss angle are very nearly the same, so
that the power factor is substantially equal to the dissipation factor for values less than 0.1.
Loss Factor. The product of the dielectric constant and the dissipation factor (or
power factor if the value is less than 0.1) is known as the loss factor.
Power Loss. The power loss in a dielectric may be considered to take place in a ficti-
tious shunt or series resistance, depending on the material, the applied frequency, and
the temperature. For a series resistance, R, the dissipation factor is
D = tan 5 = R2irfC8 = Power factor
For a parallel conductance, G, or shunt resistance, r, the dissipation factor is
D = tan 5 = rt ,., = . ,„ === Power factor
2-irfCp rZ-rrfCp
In the above formulas Ct and Cp are substantially equal for dissipation factors less than 0.1.
The power loss, P, in a parallel resistance is
m
watts
The power loss in a small series resistance is
P = &• [27r/(7fl]2 R = ZPSTrfCsD watts
Writing Cs = Cp — C in terms of K, area in square centimeters A, thickness in centi-
meters i, and the dielectric coefficient for free space 8.854 X 10 ~12,
C = 8.854 X lO-14-^ • ~
and AK
P = 0.555 X 10-12 • &• — -f-D watts
t
which may be rewritten in terms of volume in cubic centimeters, V,
(E\z
- } • V-f- (K-D} watts per cm3 per cycle per (volt per cm)2
Thus the power loss is seen to (1) increase as the square of the voltage gradient
(2) increase with the volume of material in the field; (3) increase with frequency if (K.-D]
is constant; (4) increase with the product (K-D}, the loss factor. Shunt resistance or
conductance is often the most important cause of losses at frequencies below 10 kc, since
the impedance of the capacitor is relatively high compared to the shunt resistance. At a
frequency of 100 kc the impedance will be much lower compared to the shunt resistance,
and at 1000 ke the shunt resistance of good dielectric materials is extremely high com-
pared to the impedance. In the frequency range from 1000 kc to 1000 Me the dielectric
constant and dissipation factor of good non-polar dielectric materials vary but slightly,
thus indicating a constant loss per cycle.
Polar and Non-polar Materials. A polar substance is characterized by a permanent
unbalance in the electric charges within a molecule. This unbalanced charge system is
known as a "dipole" and tends to turn in an electric field. In liquids and soft solids which
are polar, there is a free rotation of the dipoles at certain temperatures and applied fre-
quencies, causing a very high loss.
Non-polar materials have no permanent charge unbalance: though the molecule may be
distorted by an applied electric field, no tendency to rotate exists. Non-polar substances
therefore are free of sharp loss peaks as the temperature or frequency is varied, any changes
in dielectric constant and power factor occurring gradually. Whether a substance is polar
or non-polar can usually be predicted from its chemical structure. Most hydrocarbons
DIELECTRIC PROPERTIES 2-23
are non-polar and hence are numbered among the best dielectrics, e.g., polyethylene,
polystyrene, mineral wax, and oil.
Dielectric Absorption in Solids. A pure capacitance may be completely charged or
discharged almost instantaneously if the resistance in the external circuit is small. When
the capacitor contains an imperfect dielectric, current continues to flow and the charge
increases for a considerable period. The current slowly approaches a final value fixed by
the insulation resistance of the dielectric. For this reason, insulation resistance readings
are taken after the voltage has been applied for a standard time of 1 minute.
When the capacitance is discharged through a small resistance, a portion of the total
charge will be instantaneously dissipated; this has been called the "free charge." If the
circuit is opened, the capacitor will be found to have another and smaller charge known as
the "residual" or "bound" charge. Sometimes this process may be repeated two or three
times.
When an absorbing dielectric is subjected to an alternating electric field, the maximum
charge is greater than the free charge but less than the total charge in a d-c field. The
measured value of the dielectric constant decreases with increasing frequency, approach-
ing a value corresponding to the "free charge." The instantaneous charge is not in phase
with the applied a-c voltage, and a loss of energy results, heating the dielectric. The
maximum loss occurs at a frequency which is equal to the reciprocal of the time constant
of the charge or discharge current-time curve. When the frequency is increased until the
time constant for one cycle is very short compared to the charging time constant with
direct current, practically no loss remains.
The exact mechanism of absorption loss is not known, although many theories have
been suggested, such as surface charges in non-homogeneous dielectrics (Maxwell and
Wagner) , space charges (Whitehead and Joffe) , and dipoles (Debye) .
Insulation Resistance. Insulation resistance is the ratio of the applied d-c voltage to
the resultant current flowing, after 1 minute of voltage application, between two elec-
trodes embedded in, or making contact with, the dielectric. The nature of the specimen
determines whether the value represents principally surface resistance or volume resist-
ance: when thin specimens with studs or bolts as electrodes are measured at high humid-
ities, the value is more nearly representative of surface resistance; when electrodes of large
area are applied to the faces of a slab and measured at low humidities the result is more
nearly representative of volume resistance.
Surface Resistivity. Surface resistivity is the resistance between opposite edges of a
square. Since the resistance of the body of a material is always in parallel with the surface
resistance, the latter is measurable only when the volume resistance is much greater than
the surface resistance, e.g., under conditions of high humidity and large ratio of surface
to volume in the electric field.
The degree of surface contamination is an important factor since perspiration or other
surface contaminant dissolves in the condensed moisture layer and increases its conduc-
tivity. While a layer of pure water 0.1 micron thick would result in a surface resistivity
of about 3 X 1010 ohms at room temperature (a value commensurate with most wetted
insulating materials at humidities above 90 per cent), a mere trace of salt on the surface
would reduce the resistance by a factor of 10 ~3.
The temperature coefficient of surface resistivity is negative.
Volume Resistivity. Volume resistivity is the resistance between opposite faces of a
centimeter cube after the surface leakage is eliminated; it is expressed in ohm-centimeters.
Volume resistivity is calculated from the resistance between two electrodes, one of which
is completely surrounded by a guard electrode maintained at the same potential. The
current due to the surface resistance flows through the guard circuit and does not influence
the value of current in the guarded electrode circuit.
Volume resistivity has a negative temperature coefficient and often is found to have a
negative voltage coefficient. Some materials, especially those of a fibrous nature, exhibit
changes in resistance with polarity and the resistivity may change with time, owing to
polarization or to water migration. This is known as the "Evershed effect."
Dielectric Strength, of Solids. The dielectric strength of a material is the maximum
potential that unit thickness can withstand without breakdown. The value obtained
will depend upon sample thickness, temperature, applied frequency, wave form, electrode
form, area and heat conductivity, the surrounding medium, and the rate and total time
of voltage application.
In order that test values may be comparable, the American Society for Testing Mate-
rials has standardized these variables for specific classes of materials. The dielectric
strength values for a given class of material, e.g., molded thermosetting plastics, are
therefore comparable but do not bear a direct relation to the values for a different class
of material, e.g., mica or oil.
2-24 PROPERTIES OF MATERIALS
The general effect of increase in thickness is to raise the total breakdown voltage : the
increase for solid dielectrics is nearly linear for small thicknesses at room temperature but
very much less than linear for large thicknesses or higher temperatures. Elevation of
temperature invariably reduces the dielectric strength.
The peak value of the 60-cycle a-c breakdown voltage usually is less than that of the
d-c breakdown voltage. The breakdown voltage decreases with increasing frequency,
the rate depending on the loss factor of the material. Dielectric strength at 1 megacycle
may be as low as 25 per cent of the 60-cycle value.
When an electrode is sharply curved, the potential gradient at the surface is raised
according to the laws of electrostatics, and a reduction in breakdown voltage results. If
the electrode area is increased, the probability of a weak dielectric spot within the electrode
area is likewise increased, and the average dielectric strength is reduced.
The effect of time on breakdown voltage is best stated by Peek's equation:
g = £0(1 - arty
where g — dielectric strength at time t seconds.
gQ — dielectric strength at infinite time.
a — a constant.
Both go and a vary with temperature and thickness. The formula is unsatisfactory for
times less than 0.01 sec or for very long periods. *
The general effect of placing dielectrics in series is to decrease the a-c breakdown voltage,
since the voltage divides in inverse proportion to the dielectric constants if the resistivities
are high. Laminated structures, unless bonded with a medium of the same dielectric
constant or impregnated throughout with some medium, tend to have a lower dielectric
strength than that of an equivalent thickness of homogeneous material. The presence of
air or gas between laminae causes a pronounced reduction in dielectric strength.
Flashover. Flashover is an insulation failure by discharge between the electrodes over
the surface of an insulator. Sometimes the insulator is permanently damaged by the
nashover. In a uniform electric field the nashover voltage at low relative humidities
approaches the dielectric strength of air as a limit. Increase in humidity causes a surface
moisture film to form on the insulator, reducing the flashover voltage. Substances which
are wetted by water form a more or less continuous film, and the nashover values are
somewhat erratic, falling rapidly up to about 50 per cent relative humidity and then more
slowly. Non-wetted substances such as waxes, on which the moisture condenses in drop-
lets, show an almost linear, and quite consistent, decrease in nashover with increase in
humidity. Higher temperatures and lower pressures both reduce the density of the air:
therefore both factors decrease the nashover value. The flashover voltage at high humid-
ities may be from three-quarters to one-half of the sparkover voltage in the absence of
the insulator.
Arc Resistance. The power arc following a flashover or the breaking of contacts over
the insulator surface subjects the surface to extreme heat, to chemical action, and to
deposition, of electrode material. Where exposure of the insulator to arcs cannot be
avoided, it is important to know the degree of resistance to be expected. Glass, mica, and
ceramic materials are quite resistant and become permanently conductive only by deposit
of electrode material. Organic materials fail by carbonizing and become permanently
conductive even with intermittent arcing. Unfortunately, the phenolic materials are very
poor in this respect, failing in a few seconds when tested according to ASTM method
D495. Plastics, such as polystyrene, which liberate volatile monomers, tend to blow the
arc from the surface and fail in about 60 sec. Shellac, hard rubber, and vulcanized fiber
are moderately arc resistant. Vinyl plastics and methacrylates likewise are somewhat
resistant. The melamine resins are outstanding as a class: glass cloth melamine laminates
last over 180 sec. Cellulose acetates and ethyl cellulose may be formulated to exceed
180 sec resistance. Non-refractory cold-molded compounds and glass-bound mica may
last from 180 to 400 sec. Refractory cold-molded compounds last even longer, approach-
ing the ceramics. Arc-resistant varnishes are available which considerably improve the
rating of phenolic materials.
Test Methods. Methods of testing electrical insulating materials have been standard-
ized by the American Society for Testing Materials (1916 Race St., Philadelphia 3, Pa.).
A few of the more important standards are listed below :
Dielectric Constant and Power Factor ASTM D150
Dielectric Strength ASTM D149
Insulation Resistance ASTM D257
Arc Resistance ["" ASTM D495
Reference should be made to the current Index to ASTM Standards for further information.
SOLID DIELECTRIC MATERIALS 2-25
5. SOLED DIELECTRIC MATERIALS
Table 1 lists the important physical and electrical properties of solid materials useful
for electrical insulation ; it is followed by a list of trade names and additional information.
The properties given are not intended to be design values but to illustrate the range of
properties to be expected in a given class of material or a value typical of the class.
2-26
PROPERTIES OF MATERIALS
Physical Properties at 25° C
Table 1. Properties of Solid
Density,
cm3
Tens.
Sir.,
Ib
in.2
xio3
Comp.
Str.,
Ib
in.2
xio3
Mod.
of
Elas-
ticity
xio6
Flex.
Str.,
Ib
in.2
xio3
Coef.
Lin.
Ther.
Exp.
per °C
xio~6
Ther.
Cond.
per°C
xio~4
(Note
A)
Max.
Oper.
Temp.,
°C
(Note
B)
%H20
Absorp-
tion in
24 Hr
Material
(See text also)
(Note C)
1.3-1.5
2.6
2.7
2.7
1.05
1,21
1.5
0.5-0.8
1.01-1.09
1-1.17
0.9-1.07
1.2-1.3
0.96
1.32-1.39
1.35-1.6
5-6
8.5
10
7.5
Melt, pt
10.0
9-11
0.3-0.4
Melt. pt.
Melt. pt.
Melt. pt.
5-11
Melt. pt.
4.5-10
4-10
23.0
75
85
65
250-325°
20-22
38-44
025-0.4
15
5
9.0
20
22
18
3
15-20
12-16
90-100
6.9
73
7.5 .
44
54
30
5.0
60
60
60
60-80
1000
1000
1000
180?
107
148
260
0.3-0.4
0.00-0.08
0.00-0.05
0.00-0.08
Low
0.08
0.2-0.6
Very high
Allyl resin, cast . .
Alsimao- * No. 35
« No. 196
No. 211
C
0.65
1.2
Amber
Aniline formaldehyde resin
Same glass mat . .
'"V.45
14-20
Asbestos paper (dry)
Asphalt (native)
57-87° C
27-122° C
27-162° C
26-33
60.5-43.5
5.1-27
25
3; flash pt
3; flash pt
0.7-1
°C
0.5-0.57
02-0.39
200-320°
. 175-290°
12-17
C
C
50-110
" petroleum
" blown
3-4
125
0.05-0.07
Bakelite * resin, pure
Beeswax, yellow
10-18
9
80
120-160
7-14
2.3-3.2
Casein plastic
3.1-5.1
45
Celluloid * clear
Cellulose, dry
1.28-1.32
1.25-1.37
1.25-1.56
1.25-1.4
1.14-1.22
1.17-1.22
0.91-0.92
1.07
ZO-2.4
7-12
4-8
2.5-9
3-11
2.7-8.0
2.8-6.0
Melt.pt.
" acetate, film
10-30
11
11-27
7.5-2ZO
0.15-03
0.26
0.1-0.4
0.1-035
3.5-10
120-160
100
80-160
110-160
120-190
5.4-6.5
5.3-8.7
5.0-9.0
4.5-7.8
4-8
50-70
50-70
60-70
60-75
60-75
2.0-7.5
2.0-4.0
2.0-7?
1.6-2.6
1.0-1.7
Nil
0.3
0.05-5.0
" " transparent sheet
" " pigmented sheet
" " molded, gen. pur-
pose
Cellulose acetate, butyrate, molded
" propionate
5-13
2.0-13
4.8-10
65-75° C
Ceresin wax
13
8-10
100
1200
Cerex*
2-4
40-50
7
1.1-2.5
30
Cordierite ceramic
Electrose,* black
2.5-3.8
1.05-1.2
1.01-1.18
1.1-1.3
>\3
>1.05
2.3-2.9
2.9-5.9
10
20-30
300
55
50-90
35-60
125
125
Very low
1.5-3.0
1.0-2.0
1.3-2.0
<60
<65
Nil
Nil
Nil
Nil
Nil
<0.01
Nil
0.03
0.003-0.1
0.06-0.1
Enamel, vitreous
0.4-3.0
2.7-8.0
0.5-3.0
>6.0
>6.0
2-5
3-6
>0.2
Ethyl cellulose, non-rigid
8-20
0.1-0.4
0.1-0.2
4-12
'>J3'"
>12
100-140
120-180
27
27
7.5-11
8-10.5
5.6
3.8-6.2
4-6
4-6
17-25
14-20
" " rigid, gen. pur
" " cast
>30
>20
10-30
6-10
Fiber, bone, vulcanized
" commercial. . ,
8.5-13
8.7-13
Glass, crown (lime)
" flint (lead)
8.9
3.2
33
3.2
0.78
8
5-10
6.4
17
27
24
" commercial plate
2.25
Z23
2.10
2.18
3.44
2.75-3.5
3.8-3.9
40
8.86
" Pyrex,* chem. resistant
" " elec #774
10
7
500
450
800
300
300-400
300-400
200
" Multiform * # 707
" Vycor * 790
5-8
6-10
>6
0.57
Melt, pt
1.99
6.0
22-40
30-45
>20
8
8
8
15-20
14-19
13-19
13
6-12
83
Glass-bonded mica, gen. purpose . .
" " " low loss grade .
" " " injection
molded
Gummon *
0.96
190° C
1.56
100
200
4.8
Gutta percha
Hemit *
2.5-2.8
1.83-1.92
2.5-2.7
2.8
Z3
2.66
13-1.4
1.01-1.09
15.0
7.0
173
1000
Nil-0.1
Isolantite *
20-30
20
20
96
24-29
19.2
50
30
1000
1200
1100
Lava*
2.0
2.5
7.2
7-11.5
Nil
8
9
103
15-19
83
2.9
8.1
21-24
1.5
2.5
0.01
0.05-4.2
ca.60
" (Grade I)
« (Grade A)
Lavite *
0.7-1.4
ca. 15
70
ca. 1000
Lignin, sheet
Magnesium oxide, comp. powd., dry
Marble blue
2.6-2.84
135-1.4
1.45-1.55
1.4-1.5
1.9-1.95
1J-Z2
'LS'
6-7.5
3.6-7
16-29
5-4
83-213
12-13
10-16
71-91
0.26
0.4-1.9
0.6-1.8
<1.5
1.5-3.0
0.1
" white
Masonite die stock *
Melamine, alphacellulose filled
" chopped rag filled
22-25
23
38-60
20
9-14
10.5-14
31-62
7.5-93
98
98
1.6
20-45
125
" mineral filled
"Trademark names.
SOLID DIELECTRIC MATERIALS
2-27
Dielectric Materials
Electrical Properties at 25° C
Dielectric Constant
(Note D)
Power Factor %
(Not* D)
Volume Resistivity
(Note E)
Surface Resistivity,
ohms at 20-25° C
Dielectric Strength
(Note F)
Refer-
ence,
See
page 2-32
Freq.
less than
2kc
300 to
2000 kc
Freq.
less than
2kc
300 to
2000 kc
Ohm-cm
at
20-25° C
Temp.
Coef.
20-
30° C
Relative Humidity
Thick-
ness,
mils
Volts
per mil
30%
50%
90%
3.75-4.0
6.5
6.3
3.5
6.2
6.0
5.8
1.5
0.3
0.14
5.6
0.2
0.08
0.02
0.513
0.66
1.0-1.3
IG^-IO14
>1014
>1014
>IOU
5X1016
1012
1013
125
250
250
250
450
225
240
240
1400
600
450-600
100
25-50
28, 33, 39
39
39
39
1,16
39
32,39
2,7
8, 12, 17
8, 12, 17
8, 12, 17
1,12,26
1,5,8
26,33
1,12,33
12
39
12, 28, 39
39
40
32,40
39
1,5,8
33
19, 21, 39
1,12
16
40
32,40
31
1,5,12,41
1,5,12,41
15, 23, 27
15,23,27
1,16
15 "
15
27,39
27,39
39
39
39
J2
, 12
, 12
39
, 16
, 16
9
39
39
39
0
, 5, 7, 12
,5,7, 12
39
40
40
32,40
40
2.86
3.73
4.6
2.7
2.7
3.1
3.1
6X1016
3X1012
10n-1012
3.1X109
3.6
4.5-5.2
0.23
2.0
125
62
47
90
2.29
2.29
6.1X1014
6.1X1014
2X1016
2X1015
1.1X1010
4.5
0.2
1.63
5,19
2.6
16.0
4X1016
7X1014
8X1015
6X1014
5X109
5X1010
8XI014
5X1014
250-700
250
160-700
300-700
2.88
3.2
6.15
6.8
2.94
125
125
6.7-7.3
3.9-7.5
4.3-4.8
4.5-6
12
4.5-6.2
3.6-6.4
3.6-3.8
2.2
2.7
6.2-14.4
7.4-9.7
2X1010
1X109
I014
5X1010
1.8
8X1010
2X109
3.3-4.0
3.3-5
4.9
4.0-5.2
3.0-6.2
3.3-3.5
2.5
2.7
5-6
2.0-3.0
3-8
15.3
1.5-4
1-6
0.4-1.4
0.03
0.24
3.0-4.2
3-6
2-7
10-30
2800-3300
600-1300
600-1000
290-365
250-400
370-425
3X1012
1011
4-5.5
1-5.0
1.9-3.2
0.04
0.24
0.4-1.7
I0n-1013
109-1012
1010-1012
125
125
>1013
>5X1018
>8X101G
>8XI01C
>8X101G
125
250
125
500
100
600
1013-I014
'ixio14
2.3
3X1012
ixio12
8X109
2.6-3.0
2.5-4.0
3.3-3.4
2.5
2.5
6-8
7-9
0.25-0.6
10"
1012-1015
3-3.7
3.3-3.6
5-7.5
5-7.5
0.5-2.5
0.74-2.5
0.7-4.0
1.3-2.6
5.0
5.0
1.0
0.42
0.82
0.42
0.3
0.08
10n
125
250-600
2X1010
2X1010
>1013
>1013
2X1013
1014
5X1014
3.2
3.2
3XI010
3XI010
5X109
5X109
3X107
3X107
<60
>40
>175
>175
1200
860
1.0
0.45
7
7.6
3.2
8X1013
5X1010
2X106
>1013
4.8
4.9
4.7
4.0
0.2-0.4
1300
>500
>500
>180
>180
4.0
0.05
1.3
0.15-0.2
0.15-0.2
3X1013
I015
1015
1015-I017
3X1012
2.5X1015
ixio10
2.7X1014
2X108
2XI010
8.3
250
250
6.5-7.5
7.8-8.3
105-107
1.4
5X1012
2X1012
3XI08
75
200-500
50-75
320
3.0-4.9
1.8
1.2
3X1010
ixio10
ixio15
5X109
ixio11
5X108
6.1
6.1
0.18
130
1.5
2X1010
6X1011
ixio9
ixio8
75-250
<IOO
<80
235
500-650
300-700
5.6
0.3
250
250
5.3
1.0
6.4
41
0.45
37-32
3.2X1011
125
8-16
2.2
8.3
2.5-3.5
9.4
9.3
0.25-0.6
0.3-5.0
0.2
1.22
0.52
'2.9-6""
3.8-4.1
1 1-13
1X109
ixio11
2X106
I011
1012
5XI011
8X1010
8X109
3X109
4X105
ixio7
2X107
5.7-6.8
8-9.5
7.7
6.9-7.5
8-10
"7-8.2"
5.6-7.2
4.2-5.3
3.7-8
8
125
125
125
125
300
270
500
300
2XI08
5.8-6.7
11
2.8-6
I013
2-28
PKOPERTIES OF MATERIALS
Physical Properties at 25° C
Table 1. Properties of Solid
Density,
gm
cm3
Tens.
Str.,
Ib
in.2
xio3
Comp.
Str.,
Ib
in.2
xio3
Mod.
of
Elas-
ticity
xio6
Flex.
Str.,
Ib
in.2
xio3
Coef.
Lin.
Ther.
Exp.
per °C
xio-6
Ther.
Cond.
per°C
xio~4
(Note
A)
Max.
Oper.
Temp.,
°C
(Note
B)
%H20
Absorp-
tion in
24 Hr
Material
(See tact also)
(Note C)
1.18-1.2
1.18-1.2
<1.2
<1.2
16-3.2
2.6-3.2
2.6-3.2
16-3.2
16-3.2
2.3-2.4
5.8-9
6.5
4-8
5-10
10-12.5
0.3-0.5
12-14
>12
12-16
10-15
70-90
4-6
62
75
50-58
65?
500
500
500
500
1000
125
<0.4
<0.4
0.4-0.6
0.4-0.6
Methacrylate, cast, regular
" " heat-resistant.
" molded, regular ....
" " heat-resist-
ant
Mica (muscovite)
10-15
15-25
0.4-0.6
0.4
60-80
60-80
5-7
5-7
12
12
12
12
12
5-8
5-8
" U.S.A. clear
" India clear
" stained
" (Phlogopite)
" reconstructed plate
" flexible
1.1
40-50
5-9
Melt. pt.
Elongati<
jn 650%
1-1 6
150
Neoprene GN
i.06-U9
1.06-1.19
0.85-0.95
0.8-1.0
0.87-0.91
0.86-0.88
1.3-1.36
1.3-1.36
1.3-1.36
1.3-1.36
1.3-1.36
13-1.36
13-1.36
13-1.36
13-1.36
13-1.36
13-1.8
1.5-1.8
1.4-1.6
1.2-1.3
13-1.45
135
1.40-1.45
1.6-10
1.8-10
1.27-132
0.92
138
>1.05
1.05-1.07
13-1.4
11-23
23-23
12-15
I.I
1.1
I.I
2.4
12
1.07
1.1-1.4
0.91
0.92
1.5?
1.5?
Nylon * filament
18
65-90° C
0.3-0.45
12-15
100
120
" molded
Ozokerite
6.4
4.7-6.2
2 2-3.8
Paper, kraft, dry
Melt. pt.
Melt. pt.
9-15
6-10
8-12
6-10
6-8
5-8
7.5-12
6.5-10
7-11
6.5-10
5-12
7-18
14-19
6-9
6-8
6-10
6-7.5
4-10
>4.5
5-12
1.7-3.0
58° C
38-50° C
35
22
34
25
32
25
35-44
34-38
30-38
33-40
30-40
35^4
42-47
25-30
20-30
20-30
25-30
15-30
15-30
10-30
3
130-400
Paraffin
Petrolatum
0.4-2.0
0.4-2.0
0.4-2.0
0.4-10
0.4-10
0.4-2.0
035-1.5
035-1.5
035-1.5
035-1.5
035-1.5
035-1.5
1-1.2
0.7-1.0
1-1.5
1
0.7-1.2
1-1.5
3.5?
0.3-1.0
0.015
16-24
11-19
12-20
12-20
12-18
12-18
16-28
13-21
15-28
15-28
10-20
16-30
20-25
11-17
9-14
11
9-11
8-20
8-12
9-15
1.7
17-25
17-25
17-25
17-25
17-25
17-25
17-30
17-30
17-30
17-30
17-25
17-25
5-8
5-8
5-8
5-8
5-8
5-8
5-8
5-8
5-8
5-8
100-110
100-110
100-110
100-110
100-110
100-110
100-125
100-125
100-125
100-125
150-200
150-200
4-6
3-5
1.3-2
1.3-2
1-1.2
1-1.2
2-4.4
1.2-1.8
1.5-2.5
1.2-1.8
1.0-1.5
1.2-1.9
0.3-0.5
0.05-0.2
0.5-1.6
1
1-1.75
0.05-0.2
0.007-0.07
0.01-0.5
NU-0.01
0.05
<0.1
<0.1
<0.1
Nil
Nil
0.5-1.0
High
Phenolic laminates, Grade X
it (l It T>
" " XX....
" XXP...
" XXX..
" XXXP.
" CE
" " " L
« LE
" " " A
" " " AA
" " glass fabric —
" moldings, unfilled. . . .
25-60
30-75
30
30-60
25-40
8-12
4-7
5
4-7
8-20
125
135-148
135
115
150-200
135
70
75-80
82
65
65
75
200
1000
1000
90
90
90
1000 "
" " wood flour, g.p.
" " organic elec. . . ,
" " chopped rag
filled
Phenolic moldings, heat-resistant
asbestos filled
Phenolic moldings, mica filled
" cast, unfilled
28
170-210
3-5
6.2-8.1
Polyethylene
5-9
>5
>3
2-4.5
5-6
1-2
11.5-15
14
0.16-0.47
>8-I2
>8
>8
2
10-11
6-8
60-80
60-80
60-80
55
3-6
3-4
1.9
1.9
Polystyrene, general purpose
" best elcc
1.7
45-60
30-50
0.06?
7-15
5.8
25-50
25-50
4.5
4.5
4.5
21
36
Polytetrafluoroethylene
Porcelain, unglazed, wet proc
" oiled
5
7.0
Melt. pt.
1.5-10
0.13-035
32-4.2
45
200.0
70-1 00° C
2-5
11
""0.57*
0.025
Nil
Prestite *
10.15
•*
033
Quartz, fused
70-85
670
660
3.8-8.7
<65
0.03-0.08
2-4
2-4
Rubber, hard
3-3.8
natural, un vulcanized ....
" " vulcanized
" " fin<K, «i nr* r>vidr>
* Trademark names.
SOLID DIELECTKIC MATERIALS
2-29
Dielectric Materials — Continued
Electrical Properties at 25° C
Dielectric Constant
(Note D)
Power Factor %
(Note D)
Volume Resistivity
(Note E)
Surface Resistivity,
ohms at 20-25° C
Dielectric Strength
(Note F)
Refer-
ence,
See
page 2-32
Freq.
less than
2kc
300 to
2000 kc
Freq.
less than
2kc
300 to
2000 kc
Ohm-cm
at
20-25° C
Temp.
Coef.
20-
30° C
Relative Humidity
Thick-
ness,
mils
Volts
per mil
30%
50%
90%
<4
<4
<4
<4
4.5-7.5
<3
<3
<3
<3
6-7
<7
3.8-7
7
0.1-7.0
1.5-4.0
<4
1.5-4
<4
>1014
>1014
>1014
>1014
1.3X10U-
2X1017
>1012
125
500
40
40
40
40
1,7,12,16
14
14
1,14
12,14
39
39
40
39
32,40
12
12
1,5,12
10,12
40,41
40,41
40,41
40,41
40,41
40,41
40,41
40,41
40,41
40,41
40,41
40,41
39
40
40
40
40
40
40
40
39
33
40
40
40
39
1, 12, 13
19,39
12
11
11
39
1,9, 13
1,8
1, 4, 5, 12
6
6
i
125
500
10
ixio14
2X1013
8X109
6.57-8.59
7.07-7.90
5.83-9.64
5.41-6.07
3.4-4.1
0.01-0.04
1-11
1-11
1-11
1-11
6
6
1500-5700
1300-4200
1300-4100
1500-5000
950
600
0.01-0.02
0.06-8.36
0.38-7.12
2.7
I'Jxio1*
Txib1"
'9X107
4.5X1011-
0.13-0.32
2X1013
2X1011
8.3
4.5
3.2-4.5
2.4
3.5
2.2
2.2
1.6
2.7
1.0-2
0.92
0.5
4.2X1012
10U
1013
5X10U
2.2-2.5
3.3-4
2X1010
125
25
6
400
1100
750-1000
2.2
0.03
0.29-0.5
0.02
>5X1018
2X1012-
1013
>1X1018
>ixio18
100
62
62
62
62
62
62
62
62
62
62
125
125
62
125
125
125
125
125
125
125
62
500
500-700
500-700
500-700
500-700
500-650
500-650
200
400-500
200
400-500
110-225
50-150
500-600
300
200-350
550
400
300-600
550
350-450
1000-1100
4.7-5.5
4.7-5.5
3.8-4.5
3.8-4.5
,0io_,0i3
5.6XI09
4.5-5.2
4.2-5.2
7
5-6
7
4.5-5.5
5.0
3.0-3.5
2.4-3.0
10
4.5-6.5
10
3.5-5.5
' Yo9-io12'
I09-1012
I09-1012
109-1012
3XI09
9X108
12.0
1.8X109
7.5
15
0.9-1.3
3.7-4.1
5-7
5-12
6.25
5-10
5-20
6 max.
5-10
2.3
4.5-6
4.5-8
5.5
4.5-6.5
4.5-20
4.5-5
5-7
2.3
2.6
2.5-2.75
2.5-2.7
2.6-2.8
2.0
6-7
6-7.5
5-10
4-35
7.3
8-20
10-18
1.0-2.5
2.5-20
0.03-0.05
1.5-3.0
3.5-9
4.3
5-10
4-10
0.7-1.5
1.0-4.5
0.03-0.05
0.02
1012
108
1011
109-10n
109-10n
1012max.
109-1014
1016-1017
2.4X108
I.6X1010
108-1010
1014
1.7X1010
IQiQ-io12
2.4X1 010
>I013
2.5-2.75
2.5-2.7
2.6-2.8
2.0
6-7
6-7.5
2.9-4.5
5.0
3.0
7.65
0.01-0.05
0.01-0.04
0.04-0.3
<0.02
1.0-2.5
1.7-2.5
0.02-0.1
0.016-0.04
0.02-0.1
<0.02
0.8-1.0
0.8-1.0
1016
1017-1019
3.5X1019
1016
1014
108-1012
ixio9
125
125
125
80
250
250
80-120
60
60
>450
500-700
400
480
250
40-100
125-300
750
400
>1017
>1013
5X106
1.6
2X1013
6X1011
6.08
4.2
2.76
0.9
0.02
0.25-0.4
0.6-2.1
0.1-0.2
0.4
6X1011
>5X1018
5X1015-
5X1016
1018
101S-1015
1015-1015
3.5X1015
"*3.6"
ixio15
8X1014
6X1015
3X1012
5X1014
3X1015
2X108
2X1014
2X109
500
200
2.73
2.8-3.5
2.3-2.5
2.4-2.9
5.01
3.3-4.7
3
2.3-2.4
2.4-2.7
0.287
0.4-0.5
0.1-0.3
0.4
0.81
80
250-900
500-700
2-30
PROPERTIES OF MATERIALS
Physical Properties at 25° C
Table 1. Properties of Solid
Density,
gm
cm3
Tens.
Str.,
Ib
in.2
xio3
Comp.
Str.,
Ib
in.2
xio3
Mod.
of
Elas-
ticity
xio6
Flex.
Str.,
Ib
in.2
xio3
Coef.
Lin.
Ther.
Exp.
per °C
X10"G
Ther.
Cond.
per°C
xio~4
(Note
A)
Max.
Oper.
Temp.,
°C
(Note
B)
%H20
Absorp-
tion in
24 Hr
Material
(See text also)
(Note C)
Rubber, natural, 20% carbon'black
" wire insulation, Code
Perform-
ance
Rubber, wire insulation, heat-
resistant
Rubber, wire insulation, low water
absorption
Rubber, wire insulation, low power
factor
Rubber, synthetic, Buna S, gum
stock
Rubber, synthetic, Buna N, gum
stock
Rubber, synthetic, butyl, gum
stock
Rubber, synthetic,'polyisobutylene,
gum stock
Rubber, synthetic, Neoprene, gum
stock
Rubber, synthetic, polysulfide, gum
stock
Rubber, synthetic, cyclicized natu-
ral rubber
Saran,* molded
>0.5
>1.2
>1.5
>1.5
>1.5
1.5-3.2
2-4.5
3.2
0.3-1.5
1.6-1.75
0.8-1.4
Elongation >200%
Elongation >400%
Elongation >400%
Elongation >450%
Elongation >450%
Elongation 400-650%
Elongation 400-800%
Elongation 800%
Elongation 600-1 000%
Elongation 40M35%
Elongation 350-600%
50
60
75
70
70
120-140
120-140
145
60
145
90
<50
70-90
j
0.94-0.98
0.96-1.03
0.91
0.91
1.24
1.34-1.6
0.97
1.65-1.75
1.009
1.1-2.7
<0.1
00-0.1
4-6
Melt. pt.
0.9-2.0
7.5-10
45-75° C
7
0.04-0.24
15-17
160-190
2.2
6.0
Shellac
3.0
40-60
150-200
175
175
200?
<0.25
<03
" compound
28-30
Silicone glass laminate
" varnish
" varnished glass cloth
" sealing compound
" fluid
0.98-1.00
0.968-0.973
1.5-2,0
2.6-33
2.5-2.6
2.5-2.8
0.95-0.97
136
1.38
2.0-2.1
0.20-0.33
3.5-10
6.5-10
6.5-10
0.9-1.2
33
" rubber (Silastic *)
10-14.2
65-90
65-90
8
13-15
13-15
>8
18-24
18-24
10.5-20
6.5-8.5
6.5-8.5
180-220
48
60
60
432
120-200
980-1000
980-1000
60-90
80
110
95
200
300
0.2
Nil-0.1
Nil-0.1
0.2-0.5
0.05
0.03
Slate
Steatite ceramics, regular. .
" " low loss . .
Styraloy * 22
11
033
6.5
Styramic *
" HT
Melt. pt.
1.2
5-7.5
1 12.8° C
1.14
80-100
64
7
Sulfur. ...
Tegit *
3.9-4.05
15
18-20
7-8
Nil
Titanium ceramics:
Barium titanate
4
3-3.6
Calcium titanate
4-5
40-80
16-19
5-7
300
Nil
Magnesium titanate
1.45-1.6
<1.55
6-10
>6
24-30
>24
1.2-1.5
>IO
>9
25-30
7
77
77
1-3
1-3
Urea formaldehyde, cellulose filled.
" " arc resistant . .
1.24
1.26
U6
1.05-13
Tens, sta
Tens, sta
2-6
1-7
.401b.pe
. 40Ib.pt
r in. widt
riru widt
i
ii
5.0
6.0
5.0
85
90
100
60
Varnished cloth yellow
Attacked
<3.0
" " black
Vinyl plastics:
Polyvinyl alcohol
150
« butyral
3-14
1-9
>8
>6
65
ca.4.0
4.0
70-100
60-80
45
47
13
0.4-1.0
<0.15
<0.15
u caroazoie
1.22-1.65
132-136
1.4-1.55
' chloride, filled, non-rigid
Vinyl chloride-acetate:
Clear sheets
>038
>036
>13
>11
69
Sheets
* Trademark names.
SOLID DIELECTRIC MATERIALS
2-31
Dielectric Materials — Continued
Electrical Properties at 25° C
Dielectric Constant
(Note D)
Power Factor %
(Note D)
Volume Resistivity
(Note E)
Surface Resistivity,
ohms at 20-25° C
Dielectric Strength
(Note F)
Refer-
ence,
See
page 2-32
Freq.
leas than
2kc
300 to
2000 kc
Freq.
less than
2kc
300 to
2000 kc
OhnMm
at
20-25° C
Temp.
Coef.
20-
30° C
Relative Humidity
Thick-
ness,
mils
Volts
per mil
30%
50%
90%
5.97
4.5-6.0
5.0-6.0
5.0-6.0
2.75-3.0
2.75-3.0
2.7-4.4
14-19
2.1
2.2-2.4
7.5
7.5
8.8
3X1013
>5X1014
>2.7X1015
>2.0X1015
>3.2X1015
>2.7X1015
6
28,39
28,39
28,39
39
39
40
40
40
40
40
40
40
28,39
1,7,8,12
40
39
39
39
39
39
39
1,5,6,12
39
39
39
40
33
1,16
1,12
37,39
37
37
37
37
40
40
5
2, 3, II!
2,3,11
40
40
40
40
40
40
40
5.0-7.0
4.0-6.0
2.4
2.4
2.4
375-425
450-550
450-550
600-700
4.0-6.0
0.8-1.3
0.8-1.3
1.7
1015-1016
109-10n
1018
1016-1018
750
500
3.8-9.0
004
0.02-0.05
3
50
400-500
2.6-2.7
3-3.3
4.1
0.06-0.12
4.5-6.5
2.5
1016
1014-1015
IXIO16
6X1010-
2.3XI011
620
>350
900
200
4-6
S-3.7
3-8
0.81
125
0.8
200
1.5
2X1014
5xib13
ixio12
6X109
<0.5
3-3.5
3-4
2.8
2.4-2.85
0.7
0.3-0.7
0.05-0.07
0.01
7
10
100
1500-2000
500
250-300
500
5-10
200-250
200-250
700-800
800
2.8
Z4-2.82
5-7.5
<30
5.5-6.5
5.5-6.5
2.4-2.6
2.5
2.6
3.8
0.05
0.02-0.06
013-018
1013-1014
,0H
>1013
ixio6
>I09
>6XI08
6-7.5
5.5-6.5
5.5-6.5
2.5-2.6
2.55
8.6
0.13-0.3
<0.15
0.07-0.12
0.11-0.26
<63
0.1-0.2
0.04-0.1
0.05-0.15
0.04
0.02
ixio8
1014-1016
1014-I016
,020
2X1 0s
9X106
1000
250
250
125
1010-1012
uxio16
5X107
3.6-4.22
ixio17
2X1012
JQlS-IO"
4.9
1.4
ixio16
2X1012
7X1015
50
100-200
80-100
1200
165
14-18
275
6.6-8.2
<8.2
48
0.04-0.07
<0.1
<01
250
0.007
<0.1
>1014
250
100-200
7.5-9.5
7.5-9.5
4-6
<10
2.7-4.6
<4.0
512
10n-1013
>1010
10n-1012
125
125
1
10
10
300-720
300-720
700-1000
900-1200
800-1100
8X1013
ixio13
ixio9
4.5-5.5
4.5-5.5
2.5
2.0
8
6
3.0
2.0
109
6
107
10"
3.6-3.7
3.3-3.5
2.9
3.7
6
300-400
0.4
0.9
3.8
4-12
3.2-3.5
3.2-3.5
0.7
13.6
<1.3
<U
1016
500-700
600-2000
600
400
75
125
3-3.3
3-3.3
<1.9
<1.9
>1014
>1014
4X1010
2-32
PROPERTIES OF MATERIALS
Table 1. Properties of Solid
Physical Properties at 25° C
Density,
gm
cm3
Tens.
Str.,
Ib
in.2
xio3
Comp.
Str.,
Ib
in.2
xio3
Mod.
of
Elas-
ticity
xio5
Flex.
Str.,
Ib
in.2
xio3
Coef.
Lin.
Ther.
Exp.
per°C
xio~6
Ther.
Cond.
per°C
xio~4
(Note
A)
Max.
Oper.
Temp.,
°C
(Note
B)
%H20
Absorp-
tion in
24 Hr
Material
(See text also)
(Note C)
•s.7 S
Q_ 17
n ^^_A A
i? n
69
4
45
<0 15
Vinyl chloride-acetate (Contd.)
Transparent, molded
1 3-1 4
v,4
^.q
75-12
45
<0.15
Molded
i 21 4
v,C
9-12
035-085
8-12
47
<0.!5
Opaque molded
1 15-1 29
1 3
60-70
0.3-0.7
Non-rigid
1 30-1 45
1730
60-70
0.5-0.9
Filled, non-rigid
T £O1 "Jt
X A
0_1fl
flflft-fl 17
ic_j7
190
2 2
70-90
0 1
Vinylidene chloride
0 62-0 75
0 77
6-86
70
64
43-104
Wood, maple, hard
" " paraffined
ft AQ-fl Oft
0 77
6-72
130
49
5-8
" oak
3.7
12.7
90
25
4.9
120
1000
Nil
Zircon porcelain
Note A. Thermal conductivity is expressed in 10 4 X gram-calories per square centimeter per
second for a temperature gradient of 1 deg cent per centimeter. The values are typical for the tempera-
ture range 0 to 100 deg cent. The temperature gradient is perpendicular to the laminations of laminar
materials.
Note B. Maximum operating temperatures given are based on satisfactory operation under average
conditions without excessive cold flow, distortion, or shortening of the operating life of the material
In many cases it will be necessary to reduce the operating temperature in order to obtain electrical
properties or to reduce cold flow at higher unit stresses. In some cases higher operating temperatures
may be used, particularly where the material can be obtained in special grades for this purpose. If
thermal shock is involved the limit for many materials, especially the ceramics, will be much reduced.
Note C. Most of the materials listed are intended to be representative of a class rather than of a
single sample, and the ranges of values should be interpreted accordingly. Since complete mechanical
and electrical data seldom are available for a single sample or batch, and since data have been assem-
bled from many sources, it is necessary to exercise good judgment in comparing the various materials.
Values for laminated phenolic materials are those for sheets; properties of tubes are somewhat
poorer.
Note D. Where possible, the ranges of dielectric constant and power factor include the variations
to be expected over the indicated frequency ranges, although most of the values up to 2 kc are for 60
REFERENCES
1. Curtis, H. L., Insulating Properties of Solid Dielectrics, Sci. Papers Bur. Standards, No. 234
* (1915).
2. Taylor, T. S., The Thermal Conductivity of Insulating and Other Materials, Elec. /., December
1919, pp. 526-532.
3. Flight, W. S., /. I.E.E., Vol. 60, 218-235 (1922).
4. Hoch, E. T., Power Losses in Insulating Materials, Bell Sys. Tech. /., November 1922.
5. Preston, J. L., and E. L. Hall, Radio Frequency Properties of Insulating Materials, QST, Vol. 9
26-28 (February 1925).
6. Curtis, H. L., and A. T. McPherson, Dielectric Constant, Power Factor and Resistivity of Rubber
and Gutta Percha, Technologic Papers Bur. Standards, Vol. 19, 669-722 (May 1925).
7. Monkhouse, A.T Electrical Insulating Materials. Sir Isaac Pitman and Sons, London (1926).
8. Lee, J. A., and H. H. Lowry, Ind. Eng. Chem., February 1927, pp. 387-395.
9. Sosman, R. B., The Properties of Silica. Chemical Catalog Co., New York (1923).
10. Shanklin, G. B., and G. M. J. Mackay, Progress in High Tension Underground Cable Research
and Development, Trans. Am. Inst. Elec. Eng., Vol. 48, 338-372 (1929).
11. Peek, F. W,, Jr., Dielectric Phenomena in High Voltage Engineering. McGraw-Hill New York
(1929).
12. International Critical Tables. McGraw-Hill, New York (1929).
13. Barringer, L. E., Mycalex— A Moulding Material with Unique Properties, Gen Eke Rev Julv
1931, pp. 406-409. '
14. Lewis, A. B., E. L. Hall and F. R. CaldweU, Some Electrical Properties of Foreign and Domestic
Micas and the Effect of Elevated Temperature on Micas, Bur. Standards J. Research, August
1931, pp. 403-418.
15. Littleton, J. T., and G. W. Morey, Electrical Properties of Glass. John Wiley New York (1933)
16. Smithsonian Physical Tables (1933).
17. Abraham, H., Asphalts and AUied Substances. Van Nostrand, New York (1938).
18. Hartshorn, L., Plastics as Insulators, J. I.E.E., Vol. 38, 474 (1938).
19. Thurnauer, H., Ceramic Insulating Materials, Elec. Eng., Vol. 59, 451 (November 1940)
^230 481 (1940^ GIa3SOW' CoiQI)ressed Magnesia as an Electrical Insulator, /. Franklin Inst.,
SOLID DIELECTRIC MATERIALS
2-33
Dielectric Materials — Concluded
Electrical Properties at 25° C
Dielectric Constant
(Note D)
Power Factor %
(Note D)
Volume Resistivity
(Note E)
Surface Resistivity,
ohms at 20-25° C
Dielectric Strength
(Note F)
Refer-
ence,
See
page 2-32
Freq.
less than
2kc
300 to
2000 kc
Freq.
less than
2kc
300 to
2000 kc
Ohm-cm
at
20-25° C
Temp..
Coef.
20-
30° C
Relative Humidity
Thick-
ness,
mils
Volts
per mil
30%
50%
90%
3.2-3.5
3-4.0
1-4
1.8
>10U
>1014
>10U
>108
104-108
>1014
125
125
>600
>650
40
40
40
40
40
40
2, 3, 16]
1,12
3,16
36
4.7
4
4-4.8
1-3
75
75
125
>400
>400
350-2000
6-9.5
3-5.1
6-12
3-8
3-4
4.4
3-6.5
3.33
4.1
3.64-6.84
3XI010
3.6
1XI012
8X10U
2X109
600
110
3.3
9.2
3.85
0.13
ca. IOU
250
240
cycles or 1 kc, and most of the values in the higher frequency ranges are for 1 Me. For good insulating
materials, the dielectric constant does not change greatly at higher frequencies, but the power factor
may rise or fall considerably. An auxiliary table of power factors, following the main table, gives data
for some substances.
Note E. Volume resistivity has a large negative temperature coefficient. The values shown for
temperature coefficient are the ratio of the resistivity at 20 deg cent to the resistivity at 30 deg cent.
It should be remembered that at higher operating temperatures the order of merit of any two materials
may be reversed. Furthermore, the volume resistivity may be seriously reduced by prolonged exposure
to high humidities.
Note F. Dielectric strength given is for the short-time test at 60 cycles except in the case of the
ceramics, where it is given for the step-by-step method. Only those values for the same thickness are
directly comparable. Where two thicknesses are given, the higher dielectric strength applies to the
lower thickness. The dielectric strength will be much less at higher temperatures or for long times
(see discussion of dielectric strength) . In the case of laminated materials, the electric field is perpendicu-
lar to the laminations; dielectric strength with the field parallel to the laminations may be very low.
Note G. For all wood the tensile strength and flexural strength are given for forces perpendicular
to the grain, the compressive strength for forces parallel to the grain. Under Thermal Conductivity,
the first figure is perpendicular, the second parallel, to the grain.
21. Rosenthal, E., The Electrical Properties of High Frequency Ceramics, Electronic Eng., September
and October 1941.
22. Rosenthal, E., and J. E. Nickless, Ceramic High Frequency Insulators, Wireless World, Novem-
ber 1941.
23. Shand, E. B., The Dielectric Strength of Glass — an Engineering Viewpoint, Elec. Eng., Vol. 60, 41
(March 1941).
24. Simons, H. R., and C. Ellis, Handbook of Plastics. Van Nostrand, New York (1943).
25. Technical Data on Plastics Materials. Plastics Materials Manufacturers' Association, Washington,
D. C. (1943).
26. Scribner, G. K., A Ready Reference for Plastics. Boonton Molding Co., Boonton, N. J. (1944).
27. Guyer, E. M., Electrical Glass, Proc. I.R.E., Vol. 32, 743 (December 1944).
28. ASTM Standards, Vol. Ill (1944) (specifications for various plastics).
29. Englund, C. RM Dielectric Constants and Power Factors at Centimeter Wave Lengths, Bdl Sys.
Tech. J., Vol. 23, 114 (January 1944).
30. Works, C. N., T. W. Daldn and F. W. Boggs. A Resonant-Cavity Method for Measuring Dielec-
tric Properties at Ultra High Frequencies, Proc. I.R.E., Vol. 33, 245 (April 1945).
31. Barren, H., Modern Plastics. John Wiley, New York (1945).
32. Field, R. F., The Effect of Humidity on Plastics Insulation, Plastics and Resins, September 1945.
33. Brouse, H. L., A Review of Plastic Materials, Proc. I.R.E., Vol. 33, 825 (December 1945).
34. Bass, S. L., and T. A. Kauppi, Silicones— a New Class of High Polymers of Interest to the Radio
Industry, Proc. I.R.E., Vol. 33, 441 (July 1945).
35. Plastics Design is Given Impetus by Engineering Classification (SPI), Elec. Mfg., Vol. 36, 128
(November 1945).
36. Russell, R., and W. C. Mohr, Zircon Porcelain, New Insulation for New Products, Elec. Mfg.,
January 1946.
37. Wainer, E., High Titania Dielectrics, Electrochem. Soc. Trans., 1946.
38. Warner, A. J., Problems in the Manufacture of Ultra-high-frequency Solid-dielectric Cables, Proc.
I.R.E., Vol. 1 of Waves and Electrons section, p. 31W (January 1946).
39. Manufacturers' catalogs, circulars, and other data.
40. References 24, 25, 26, 28, 31, 33, 35, 39.
41. NEM A Standards.
2-34
PROPERTIES OF MATERIALS
Auxiliary Table. Power Factor of Insulating Materials at High Frequencies
(Approximate representative values)
Material
Frequency
60 cycles
1 kc
1 Me
10 Me
100 Me
1000
Me
10,000
Me
0.0002
.0002
.00024
.0003
.0002
.0005
0.0002
.0002
.0002
.0002
.0002
.0003
.0004
.0004
.0005
0.0002
.0002
.0002
.0002
.0002
.0003
.00035
0.0002
.0002
.0002
.0002
.0003
.0003
.00035
0.0001
.0002
.0002
.0002
.0004
.0004
0.0001
.004
Polytetrafluoroethylene ....
0.0002
.00024
.0003
.0004
.0004
.0014
.0005
.001
.0002
.0005
.0014
.0004
.0004
.0005
.0008
.0008
.0008
.0009
.001
.0015
.0034
.004
.005
.006
VJ , MI£M
.06
.0026
.0013
.004
.0008
.0009
.003
.002
.0035
.004
.006
.006
.015
.01
Polyvinyl carbazo e
.003
.0021
.003
.004
.005
.0033
.006
.014
.02
.04
.0014
.002
.003
.006
.004
.006
.005
.007
.0086
.03
.015
.0011
.0015
.003
.005
.004
Steatite low loss
.0022
.015
.003
.006
.0025
\niline formaldehyde
.008
Glass Pyrex
Rubber hard (best)
Ethvl cfllulos? (best)
.007
.025
.03
.03
.015
.006
.025
Phenolic, mica filled (best) . . .
.010
.01
orce in, e p oc
.03
Vinyl resin (hard)
.007
Phenolic glass base
.011
.035
.013
.04
.018
.05
.02
.080
.024
.04
Phenolic, paper base
.05
.04
ADDITIONAL INFORMATION ON SOLID DIELECTRIC MATERIALS.
Acrylic Resins and Acrylates. Designations used for thermoplastic polymers derived from acrylic
acid (CH3 : CHCOOH), methacrylic acid [CH2 : C(CH3)COOH], or allied materials. The most impor-
tant are the methyl methacrylates, q.v. Acrylics may be vulcanized to reduce thermoplasticity.
Alkyd Resins. Resins derived from reaction of polybasic acids with polybasic alcohols, glycerol
and phthalic anhydride being the principal materials in use. They are used chiefly for varnishes and
other coatings. Trade name: Glyptal.
Allyl Resins. A group of plastics derived from allyl alcohol (CH2 : CHCHaOH). The resins are
marketed in the form of cast transparent sheets and rods, and in the form of liquid monomers which
are polymerized with the aid of a peroxide catalyst and heat, but no gases or vapors are emitted. The
resin is thermosetting in nature with good electrical properties which are maintained at elevated tem-
peratures. Index of refraction, UD, is 1.49 to 1.51. Light transmission is over 91 per cent. Specifica-
tions: ASTM D819. Trade names: Allymer, MR Resins, Kriston.
Allymer * CR-39 et al. Pittsburgh Plate Glass Co. Allyl resins.
Alsimag.* American Lava Corp. Steatite, cordierite, and other ceramic bodies.
Alvar.* Shawinigan Products Corp. Polyvinyl acetal resin.
Amber. Yellow or orange fossil resin found on the shore of the Baltic Sea. High insulation re-
sistance makes it an excellent insulator for electrometers.
Amphenol * 912. American Phenolic Corp. Polystyrene sheet, rod, and tubes.
Amphenol * 912B. American Phenolic Corp. Methacrylate sheet, rod, and tubes.
Aniline-formaldehyde Resins. Derived from aniline and formaldehyde and fabricated by casting-
and very limited molding under heat and pressure. The resin is but slightly thermoplastic, and parts
are usually made by machining sheet or rod stock. Color is reddish brown. Insulation resistance is
high and dielectric losses are low over a wide frequency band. Trade names: Dilectene, Cibanite.
Annite.* Spaulding Fibre Co. Thin vulcanized fiber (fish paper).
Aroclors.* Monsanto Chemical Co. Chlorinated diphenyl resins and oils.
Asbestos, A hydrated magnesium silicate mineral in fibrous form. Two distinct groups of min-
erals are described as asbestos: amphibole, or hornblende asbestos, in various subgroups, most of which
contain iron and have harsh and springy fibers, relatively weak and non-flexible; and serpentine as-
bestos, the principal subgroup consisting of chrysotile, so-called Canadian asbestos, which has soft*
fine, strong fibers, suitable for manufacture of asbestos textiles. Chrysotile asbestos is stable up to.
temperatures of 400^ to 500 deg cent and may be useful at still higher temperatures. It is not a par-
ticularly good electrical insulator and has very high losses when moist but is valued chiefly for its fire
resistance and its heat resistance. Asbestos products should not be allowed to come into contact with
fine wires since corrosion may result.
* Trademark names.
SOLID DIELECTRIC MATERIALS 2-35
Asbestos Paper. Made by felting asbestos fibers, often with some rag fibers for additional strength.
It is employed normally only as a flame barrier or for heat insulation and should not be depended upon
for electrical insulation.
Asbestos Textiles. May contain up to 6 per cent total iron content and as much as 2 per cent
iron in a magnetic form. A higher grade known as "non-ferrous," containing less than 1.75 per cent
total iron and less than 0.75 per cent magnetic iron, is available. Non-impregnated asbestos products
are extremely hygroscopic. In order to avoid absorption of moisture, the products often are treated
with varnishes or oils, but impregnation reduces the maximum operating temperature sharply.
Asbestos Wood. Asbestos combined with Portland cement to form dense sheets (Transite). Also
combined with magnesia and cement in an insulating board impregnated with a black insulating
compound (ebony asbestos wood).
Asbestos Ebony.* Johns-Manville Co. Asbestos fiber and binding cement impregnated with
compound.
Asphalts, Natural. Native asphalts are roughly divided into relatively pure deposits containing
less than 10 per cent mineral matter and those containing a large amount of mineral matter. Both
types of deposit contain water, but in the latter group the water is often in emulsified form. The
water content may be as high as 40 per cent. It is very difficult to separate any but the largest particles
of mineral matter by heating. Asphalt is used for potting and impregnating compounds, in the manu-
facture of varnishes and japans, and for the insulating covering of cables. It is closely related to petro-
leum asphalt and asphaltites, which are used for the same purposes. Refined Trinidad asphalt melts
at 87 deg cent and contains about 38 per cent mineral matter. Bermudez asphalt melts from 57 to
87 deg cent and contains about 4 per cent mineral matter.
Asphalts, Petroleum. A "rubberlike" asphalt of almost any desired melting point up to 150 deg
cent. The residue from the distillation of asphaltic or mixed-base petroleums. Sometimes called
residual pitches or asphalts. Have greater purity and uniformity than natural asphalts. Used for
potting, impregnating, etc. Some residual asphalts weather very badly when exposed to sunlight.
Petroleum asphalt may be "blown" with air and steam to oxidize the asphalt partially and to increase
the melting point. They also may be modified by adding rosin derivatives to increase the fluidity at
high temperatures without drop in melting point.
Asphalts, Sulfurized. Sulfur has a hardening action on asphalt, similar to vulcanization of rubber
in some respects. Used in corona-resisting wire insulation.
Asphaltites. Asphaltlike substances but much harder; have melting points above 120 deg cent.
Not as soluble in petroleum hydrocarbons. The most important varieties are: gilsonite, m.p. 130
deg cent; glance pitch or manjak, m.p. 160 deg. cent; and graharnite, m.p. 175 deg cent Another
group of asphaltites containing so-called pyrobitumens are practically infusible. Elaterite, wurtzilite,
albertite, and impsonite are members of this group and are almost insoluble in the usual solvents.
The first group is used in the manufacture of varnishes and japans.
Bakelite.* Bakelite Corp. Phenolic, cellulose acetate, polystyrene, urea, and other resins, plastics,
and molding powders.
Balata. A rubberlike natural material similar to gutta-percha and used for similar purposes. M.p.
150 dec cent. Dielectric constant 2.6 to 3.5, depending on purity. May be deresinified to improve
properties for use in submarine cables. See Kemp, J. Franklin Inst., Vol. 211, No. 1, p. 37.
Beeswax. A white to yellow insect wax. Plastic at 30 deg cent. Melts from 62 to 64 deg cent,
A good electrical insulator. Has a large negative coefficient of volume resistivity; is bleached by
sunlight and turns brown with age.
Beetle.* American Cyanamid Co. Urea formaldehyde molding powders.
Buna N. Synthetic rubber made from butadiene and acrylonitrile by emulsion polymerization.
Heat-, oil-, and solvent-resistant, but electrical properties are not good. Trade names: Hycar OR,
Perbunan, Ch&migum.
Buna S. Common type of synthetic rubber made from butadiene and styrene by emulsion polymer-
ization. Rubber made in government plants is known as GR-S. Insulation fully equal to that of
natural rubber in electrical properties can be made from Buna S although the mechanical properties
are not quite so good. Its general behavior is quite similar to that of natural rubber.
Butacite.* E. I. du Pont de Nemours & Co. Polyvinyl butyral plastics.
Butvar.* Shawinigan Products Corp. Polyvinyl butyral plastics.
Butyl. A synthetic rubber made from isobutylene and butadiene by polymerization at low tem-
peratures with a catalyst. It has excellent electrical properties, good resistance to heat, ozone, and
corona, and low permeability to gases but is inferior to natural rubber in strength. When made in
government plants it was known as GR-I.
Casein. Prepared from skim milk by rennet treatment and hardened by soaking in formaldehyde.
Before hardening it can be extruded and pressed; after hardening it is readily machined. It softens in
hot water at 100 deg cent and can be blanked or molded to a limited extent. It is not a particularly
good electrical insulator but is occasionally useful for small parts. It is readily colored either before or
after fabrication.
Catalin.* Catalin Corp. Cast phenolic resins.
Cellophane.* E. I. du Pont de Nemours & Co. Regenerated cellulose film, lacquered to reduce
moisture transmission.
Celluloid.* Celanese Plastics Corp. Cellulose nitrate.
Cellulose Acetate. A thermoplastic prepared by treatment of cotton linters or other cellulose with
acetic anhydride and acid and the addition of suitable plasticizers. Variation of processing and plasti-
cizer gives a wide range of molding flows and of the heat resistance, flow mobility, and other properties
of the product. Available in all colors and in the forms of film, sheet, rod, and molding powders for
* Trademark names.
2-36 PROPERTIES OF MATERIALS
compression and injection molding or for extrusion. Films and sheet of electrical grade are non-cor-
rosive to fine copper wires even under conditions favorable to electrolysis and are superior for coil con-
struction. Some molded materials contain volatile plasticizers and shrink in time or with heating. The
heat distortion point of many grades is also quite low. Cellulose acetate is not attacked by oils but is
dissolved by ketones, esters, and other solvents. Specifications for sheets: ASTM D786; for molding
powders, ASTM D706. Trade names: Fibestos, Lumarith, Plastacele, Tenite I.
Cellulose Acetate-butyrate. Similar to cellulose acetate except that it is a mixed ester of cellulose.
Less plasticizer is required to obtain molding flow, and heat resistance is improved slightly. It is widely
used in tape form for wire insulation and as a molding powder. Specifications for molding powders:
ASTM D707. Trade name: Tenite II.
Cellulose Nitrate. Also known as pyroxylin and Celluloid. It is made by nitrating cotton linters
or wood pulp and adding suitable plasticizers such as camphor. Basically highly inflammable, but
appropriate plasticizers reduce the inflammability. Very tough and is water- and chemical-resistant.
Marketed as sheets, rods, tubes, and molding compositions. Specifications for sheet, rod, and tube:
ASTM D701. Trade names: Celluloid, Pyralin, Nitron, Nixonoid.
Cellulose Propionate. A new pkstic similar to cellulose acetate but with improved impact strength
and excellent dimensional stability. Good electrical properties and low water absorption. Trade
name: Fcrticel.
Celeron.* Continental-Diamond Fibre Co. Macerated-fabric-base phenolic moldings.
Ceramics. Electrical ceramics include materials sintered, fused, or fired at high temperatures, such
as porcelain, steatite, cordierite, glass, glass-bonded mica, titanium and zircon ceramics, q.v. Ce-
ramics are characterized by heat resistance, permanency of dimension, low water absorption, low ther-
mal expansion, and excellent electrical properties. Care is required in mounting ceramic parts since
the modulus of elasticity is high and a slight bending develops high stresses. With the exception of
glass-bonded mica, ceramics are not machinable by normal methods and are normally cast, molded,
pressed, or extruded and machined in the unfired state and then fired at a high temperature. Since
firing shrinkage is around 12 per cent, tolerances are not close, usually of the order of 1 per cent of the
dimension. A limited amount of grinding can be done after firing.
Ceresin. A white or yellow wax, with exceptional dielectric properties. Used extensively alone
and mixed with other waxes. M.p. 65 to 67 deg cent. ' Soluble in oils and petroleum distillates.
Very water-resistant and has high surface resistivity.
Cerex.* Monsanto Chemicals Co. Polystyrene copolymer.
Chatterton's Compound. Fusible composition of gutta-percha, rosin, and tar used in submarine
cable construction for sealing cable ends, etc.
Copaline.* American Phenolic Corp. Solid-dielectric r-f cables.
Cordierite Ceramics. Consist principally of the crystal cordierite, a magnesium aluminum silicate,
and are characterized by a very low coefficient of thermal expansion and a power factor much higher
than that of steatites. Trade name: Alsimag 72 and 208.
Co-ro-lite.* Colombian Rope Co. Sisal-fiber-reinforced phenolic materials.
Corprene.* Armstrong Cork Products Co. Cork-loaded neoprene sheet in various grades.
Dilectene.* Continental-Diamond Fibre Co. Aniline formaldehyde sheets and rods.
Dilecto.* Continental-Diamond Fibre Co. Laminated phenolic sheet, rod, and tubes.
Dri-film.* General Electric Co. Silicone treatment for ceramics.
Durez.* Durez Plastics and Chemicals, Inc. Phenolic resins and molding powders.
Durite.* Durite Plastics, Inc. Phenolic and furfural resins.
Ebonite. Another name for hard rubber.
Empire.* Mica Insulator Co. Varnished cloth, sheet, and tape. Silk, rayon, Fiberglas, 2 to 40
mils thick.
EnameL General term for a substance producing a colored glossy coating. Organic enamels are
made by pigmenting or coloring lacquers or varnishes, and inorganic enamels by pigmenting low-
melting glasses. (See discussions below.)
Enamel, Varnish. Pigmented varnishes or varnishes colored by asphalts or colored resins. Varnish
enamels may either dry in air in 4 to 16 hr, depending on the type, or be compounded to dry by baking
from 2 to 8 hr at 100 to 150 deg cent. The baking types usually have better adhesion and hardness and
higher dielectric properties. The japans are varnish enamels made with asphalts for baking.
Enamel, Vitreous. A silicate or borosilicate glass with the melting point lowered by the addition
of various fluxes, such as metallic oxides and salts. Some metallic oxides are used for coloring the enamel
and others to increase the opacity. The enamel is usually applied in two or more coats when freedom
from pmholes is desired. The same composition may be used for all coats in some cases, although
specially formulated ground coats are usually superior. The enamel coats are applied by dipping or
spraying, using a suspension of the finely ground enamel, known as frits, in a clay-and-water medium.
For flat work the powdered frits are sometimes sieved onto the work in the so-called dry process. The
coats are "fired" at temperatures up to 850 deg cent for periods of 3 to 30 min. The temperature and
time are critical for a given composition of enamel and for the size of the enameled object. Some en-
amels have very satisfactory dielectric properties and may even be used for the dielectric of small adjust-
able capacitors, but the major electrical use is the manufacture of vitreous enamel resistors. For this
use the formula is carefully adjusted to obtain a coefficient of thermal expansion suitable for the wire
and coil forms, to prevent fracture of the wire with cycles of heating and cooling.
Enamel Wire. Enamel for insulating wire is usually a varnish enamel. A hard, tough, and flexible
covering is produced with a high dielectric strength. The enamel thickness varies from 0.0001 to
0.0015 in., depending on the wire size. Enamel is suitable for continuous operation at 105 deg cent
Wire enamels vary slightly in resistances to oils and solvents. The better grades are suitable for con-
* Trademark names.
SOLID DIELECTRIC MATERIALS 2-37
tinuous use in mineral oil up to 80 deg cent; 48 hr at 105 deg cent should have no visible effect. Most
varnish and lacquer solvents will attack wire enamel to some degree if the contact is prolonged. It is
important, therefore, to expel the solvents from varnish impregnation or cementing processes with
reasonable promptness. It is necessary in most cementing processes for the solvents to attack the
enamel slightly in order to secure a good bond. Wax impregnation has practically no effect on the
enamel, but impregnation with asphaltic compositions may cause a severe attack on the enamel. The
enamel is moderately resistant to abrasion and pressure, and wire may be random wound for some uses
where a few shorted turns are allowable. It is also used successfully on core plates where it is subjected
to considerable pressure and is occasionally filled with mica dust to improve the resistance to pressure.
Ethocel.* Dow Chemical Co. Ethyl cellulose molding powder.
Ethofoil.* Dow Chemical Co. Ethyl cellulose film.
Ethyl Cellulose. Prepared by replacing the hydrogen of cellulose hydroxyl groups with the ethyl
group by means of ethyl chloride or ethyl sulf ate. It is thermoplastic and is tough and flexible through
wide ranges of temperature. It is very stable to heat and light and has excellent electrical properties.
It is available in "hot-melt" compounds, in casting compositions (Thermocast *) , in films, as non-rigid
sheets and extrusions, and as molding compositions. The electrical properties are well retained under
moist conditions and actually may improve with increasing temperatures, contrary to the general rule.
Specifications for non-rigid: ASTM D743; for molding: ASTM D787. Trade names: Ethocel, Lumartih
EC, Chemaco, Hercules EC.
Fiber, Vulcanized. Manufactured by treating rag paper with zinc chloride, pressing into sheets,
and thorough washing. Fiber will absorb water up to about 60 per cent if immersed for a sufficient
length of time and will increase to nearly double the thickness. Solvents and oils have practically no
effect on fiber. Fiber has a natural moisture content of 5 to 6 per cent at 40 to 60 per cent relative
humidity, which will decrease at low humidities and increase at high humidities. Heating at 80 to
100 deg cent for long periods will dry out and warp the fiber and impair the flexibility and toughness.
From 100 to 170 deg cent the drying is very rapid, and the fiber will become brittle in a few hours.
Above 170 deg cent the material will char on long heating. It chars in a short time at 200 deg cent. The
maximum safe operating limit is about 150 deg cent. Fiber is made in gray, black, red, and white, but
there is little difference in the properties due to the colors of the same grade of stock. Grade differences
are due to selection of rags, increased pressure in order to increase density and hardness, and more
careful processing. The highest grade is the electrical grade made in thin sheets for use in slot insula-
tion, etc., and commonly known as "fish paper." This grade has exceptionally high dielectric and
mechanical strength and a density of about 1.3. Hard fiber (bone fiber, horn fiber) has a density of
about 1.3, and is considerably harder than the commercial grade. The commercial grade has slightly
lower mechanical strength but about the same dielectric strength and shows considerably higher water
absorption on 1-hr immersion. A grade especially made for forming and swaging contains glycerin to
soften the material by retaining moisture. It can be swaged, spun, and formed readily for bushings,
grommets, etc. All grades are readily machinable and can be punched and also formed dry to a limited
extent. For more severe operations, the sheets can be soaked in water and formed in heated dies. The
fiber bends best parallel to the grain.
Fiberglas.* Owens-Corning Fiberglas Corp. Glass yarn and textiles.
Fibestos.* Monsanto Chemical Co. Cellulose acetate.
Fibron.* Irvington Varnish and Insulator Co. Flexible plastic products. Polyethylene tape and
tubing.
Fish Paper. Common name for superior grade of thin vulcanized fiber, also known as tarpon paper,
leather paper, leatheroid, and fiberoid. It is usually supplied in a dark gray color.
Flamenol.* General Electric Co. Polyvinyl chloride wire insulation.
Formex.* General Electric Co. Polyvinyl formal magnet wire insulation.
Formica.* Formica Insulation Co. Phenolic laminates.
Formvar.* Shawinigan Products Corp. Polyvinyl formal.
Forticel.* Celanese Plastics Corp. Cellulose propionate plastic.
Fortisan.* Celanese Corp. of America. High-strength regenerated cellulose yarns.
Fullerboard. Another name for pressboard.
Furfural Resins. Phenol and furfural react to form resins similar to phenol-formaldehyde resins
but generally dark in color. They are used for transfer molding and cold molding. They withstand
high temperatures and have comparatively good arc resistance. Trade name: Durite.
Gelva.* Shawinigan Products Corp. Polyvinyl acetate.
Geon.* B. F. Goodrich Chemical Co. Polyvinyl chloride and vinyl vinylidene chloride.
Gilsonite. Variety of natural asphalt. M.p. 122 to 188 deg cent.
Glass. Physically, glass is an amorphous, undercooled liquid composed of silica and metallic sili-
cates and hence has no crystal structure or sharp melting point. The plastic nature of glass at elevated
temperatures permits fabrication by drawing, blowing, and pressing, as well as by casting. Only simple
shapes can be molded. All glass must be carefully annealed to prevent residual stresses which reduce
the strength, or surface-chilled in a controlled manner, as in so-caned tempered glass, so that the residual
stresses will increase the strength. Since glass has a high elastic modulus and no internal structure to
interrupt stress patterns, it is extremely sensitive to stress concentrations. Glass parts must be care-
fully designed, and surface damage must be avoided. Exclusive of glasses designed for sealing purposes,
lime glass, lead glass, borosilicate glass (Pyrex types), and high-silica glass (Vycor) are the principal
electrical glasses. The borosilicate and high-silica types have lower coefficients of thermal expansion,
giving improved resistance to thermal shock. Electrical glasses have high dielectric strength and vol-
ume resistivity and low power factor. These properties depreciate with rising temperature, and at
temperatures from 150 to 200 deg cent a rapid rise in power factor and decrease in dielectric strength
* Trademark names.
2-38 PROPERTIES OF MATERIALS
begin. The high-silica glasses are superior in this respect. The surface of glass is readily wetted by
water so that the surface resistivity is seriously reduced by relative humidities above 70 per cent. This
is perhaps the most serious defect of glass as an electrical insulator, but recent work has indicated that
leakage may be considerably reduced by treatment with sih' cones, q.v. The Multiform process, in
which glass is powdered, pressed to shape, and fired like porcelain, makes possible the production of
complicated parts to tolerances of 1 to 2 per cent and permits the use of high-silica glasses with very
low losses and low thermal expansion. Recently developed techniques permit the firing of metallic
coatings on glass, which may be used as circuit conductors, for soldered connections, or hermetic seal-
ing by soldering. By alteration of the composition of glass, the thermal expansion may be matched to
certain metals so that dependable seals resistant to thermal shock can be produced. Lead-through
seals are available in single or multiple form, which may be soldered in a metal container to give a
hermetic seaL
Glass Textiles. Glass drawn into thin filaments (2 to 3 X 10~4 in. diameter) has an enormous tensile
strength (4 to 5 X 105 Ib per sq in.), owing to an absence of shearing stresses. Glass textiles (Fiber gl 'as *)
are made from glass yarn of two basic types: continuous-filament yarns made by hot drawing of fila-
ments from glass "marbles" in a special machine, and staple yarns made from staple fiber produced by
steam drawing of molten glass into fibers varying from 4 to 18 in. in length. The individual fibers are
lubricated and combined into yarns of various constructions. Glass textiles are available as tapes,
cloth, sleeving, cords, and yarns for serving or braiding. Outstanding uses for glass textiles have been:
(1) high-strength plastic laminates; (2) fireproof braiding for insulated wire; (3) varnished glass cloth;
(4) serving for magnet wire. Advantages of glass textiles in these and other services are greater re-
sistance to heat, longer life, non-inflammability, increased moisture resistance, and high mechanical
strength.
Glass-bonded Mica. Ground mica bonded with a low-melting glass, chiefly lead borate, and some-
times with the addition of cryolite (sodium aluminum fluoride). The material is hot-pressed at 600 to
700 deg cent to the required form. Certain types can be injection-molded. Metal inserts can be molded
in place, in some cases for hermetic sealing purposes. It is also possible to cast aluminum around the
material or to use it as an insert in plastic molded parts. It can be readily machined with carbide tools,
or with ordinary tools for small quantities, to close tolerances. Glass-bonded mica has excellent elec-
trical properties, good mechanical properties, low coefficient of expansion, and stability in dimensions
•up to 300 deg cent. Electrical properties do not deteriorate rapidly with rising temperature or under
moist conditions, except that the surface resistivity of grades containing fluorides may be very low at
high humidities. Under condensation conditions, the fluoride constituents are dissolved and may cor-
rode metal parts. Polishing and waxing the surfaces will eliminate this condition but will reduce the
arc resistance. Special varieties of glass-bonded mica (Mycalex K *) are available with controlled dielec-
tric constants between 8 and 20. Specifications: Army-Navy Specification JAN-I-10, Grade L-3 or
L-4. Trade names: Mycalex, G. E. Mycalex, Mycroy, Turx.
GlyptaL* General Electric Co. Alkyd resins and products such as varnishes, cements, varnished
cloth, etc., made therefrom.
Gummon.* Garfield Mfg. Co. Asbestos coal-tar moldings.
Gutta-percha. A grayish-white to brown plastic substance but not elastic like rubber. Can be
molded under pressure at 60 to 100 deg cent and melts from 120 to 140 deg cent. It vaporizes above
190 deg cent. Partly soluble in ether, carbon tetrachloride, benzol, chloroform, and carbon bisulfide;
insoluble in water. Can be vulcanized with sulfur or sulfur chloride like rubber, forming a hard sub-
stance, but it is nearly always used unvulcanized. It is rather easily oxidized in the air and becomes
brittle and yellowish gray. It is principally used for the insulation of submarine cables and ia generally
applied uncompounded by a tubing machine or in strips like rubber. The power factor of gutta-percha
is mayi'mrim at room temperatures, so that the dielectric loss in actual service at sea-bottom tempera-
tures is quite low. If the insulation is prepared with about 1.5 per cent moisture content, which is
close to the saturation value in sea water, the constants do not change much in service. The life is
very satisfactory under water but is not very satisfactory in air.
Halowax.* Bakelite Corp. Chlorinated naphthalene liquids and waxes for impregnating.
Hard Rubber. See Rubber, hard.
Hemit* Garfield Mfg. Co. Cold-molded refractory materials.
Herculite.* Pittsburgh Plate Glass Co. Tempered glass products.
Hycar.* Hycar Chemical Go. Synthetic rubber in various grades, distinguished by suffix letters
and numbers.
Insurok.* Richardson Co. Phenolic and urea laminates.
f Isolantite.* Isolantite, Inc. Steatite ceramics.
Jute. A long bast fiber employed in cordage and rough textiles. Considerably used as a filler and
core in cords and cables. Commercial jute often is softened and rendered less brittle by impregnation
with -mineral oiL Jute loses its strength when damp.
Kaolin. Also called china clay. An aluminum silicate clay free from iron, used in the manufacture
of white porcelain. Valuable as a packing material around heating coils, etc.
Kriston.* B. F. Goodrich Chemical Co. AUyl monomer.
Lamicoid.* Mica Insulator Co, Phenolic laminates.
Laminates, Layers of paper, cloth, or glass cloth impregnated with resin and pressed under heat
and high pressures. Resins are usually thermosetting, but thermoplastic resins have been used Low-
pressure laminates use resins which give off little or no gas or vapor during curing, and pressure just
sumcient to hold the mass in contact is required. Very large, shaped parts can be produced by employ-
ing inflated or evacuated rubber bags to supply the low pressures needed. Knitted cloths are often
used to allow stretching where required. Contact laminates can be made with still lower pressures (as
* Trademark names.
SOLID DIELECTRIC MATERIALS 2-39
low as 1 Ib per sq in.). Trade names of materials employed for contact laminating are: Laminae,*
American Cyanamid Co.; Thalids* Monsanto Chemical Co.; Bakelite Copolymer Resins,* Bakelite
Corp.; Selectron,* Pittsburgh Plate Glass Co.; Vibrins,* Naugatuck Chemical Co. The electrical
properties of many of these low-pressure laminates are excellent. They were employed for such appli-
cations as radomes during the war. Properties of sample laminates: dielectric constant 3.54 to 4.59 at
1 Me; power factor 0.0075 to 0.0105 at 1 Me.
Latex. An emulsion of rubber, synthetic rubber, or synthetic resin in water, depositing a solid
film on evaporation.
Lava.* American Lava Corp. Mineral talc machined to shape and fired at high temperatures.
Lavite.* D. M. Stewart Mfg. Co. Steatite ceramic.
Lenoxite.* Lenoxite Div., Lenox, Inc. Steatite ceramic.
Lignin. Lignin is the binding material in wood. Two types of plastic are made from lignin. In
one type the whole wood is used; steamed chips are exploded by sudden pressure release and are pressed
into boards under high pressure (Masonite,* Benalite,* Masonite Corp.). In the other type the sepa-
rated lignin, usually a byproduct of paper manufacture, is combined with other materials, such as
amines, furfural, or phenol, to form a thermosetting resin which maybe combined with various fillers,
or is used to impregnate paper which is hot-pressed into laminated boards (Lignolite *) . Lignin also
is used as an extender for phenol-formaldehyde molding compounds.
Lignolite.* Marathon Chemical Co. Lignin plastic sheets.
Loalin.* Catalin Corp. Polystyrene.
Lucite.* E. I. du Pont de Nemours & Co. Methyl methacrylate sheet and molding powders, also
in heat-resistant grades.
Lumarith.* Celanese Celluloid Corp. Cellulose acetate and ethyl cellulose products.
Lttstron.* Monsanto Chemical Co. Polystyrene molding powders.
Magnesium Oxide. Compressed magnesium oxide is used in the insulation of heating units and,
in Europe, for heat-resistant coaxial conductors (Pyrotenax *). Single or multiple conductor cables are
made by packing magnesium oxide preforms and the conductors inside a copper tube and drawing the
assembly to a smaller size. As a r-f coaxial line the losses are higher than those of polyethylene insula-
tion, and the ends must be well sealed against moisture. It is electrically smooth compared to an
insulator-spaced air line.
Makalot.* Plastics Div., Interlake Chemical Co. Phenolic resins and compounds.
Masonite* Die Stock. Masonite Corp. Exploded wood fiber, densified under high pressure.
Melamine-formaldehyde. Thermosetting resins prepared by reaction of formaldehyde, melamine,
and sometimes dicyandiamide; the latter two are derived from calcium cyanamid. These resins are
heat- and arc-resistant and have excellent electrical properties and low water absorption. Alpha cel-
lulose, chopped rag, and mineral fillers are used in various compounds. Specifications: ASTM D704.
Resin trade names : M elmac, Resimene, Plaskon Melamine.
Melamine Glass Laminates. These laminates are characterized by high arc resistance and great
mechanical strength. They are also heat-resistant and burn with some difficulty. The fumes from the
burning laminate are said to be less toxic than those from phenolics ; hence these laminates were used
for combat-vessel equipment. The high-frequency properties are not outstanding and are not con-
trolled in production. Specifications: Joint Army-Navy Spec. JAN-P-13 Type GMG.
Melmac. American Cyanamid Co. Melanune-fonnalaehyde resins and molding powders.
Methacrylates. These resins are members of the acrylic or acrylate resin group. The most im-
portant member is methyl methacrylate. This plastic is produced by the reaction of acetone and hy-
drogen cyanide to form acetone cyanhydrin, which is allowed to react further with methyl alcohol to
produce methyl methacrylate monomer [CH2 * C(CE3)COOCHg]. This monomer is polymerized by
the aid of peroxide catalysts and heat. The polymers are characterized by great optical clarity, light
transmission of 92 per cent, high refractive index of 1.48 to 1.51, stability to light and weather, and
good mechanical and electrical properties. Arc resistance is high; vapor from the plastic actually tends
to quench arcs. Power factor and dielectric constant decrease with increasing temperature and fre-
quency instead of exhibiting the normal increase. Methyl methacrylate in common with other thermo-
plastics has a low heat distortion point. Heat-resistant grades are available that will withstand boil-
ing in water. Specifications for sheet, rods, and tubes: ASTM D702; for molding compounds: ASTM
D788. Trade names: Plexiglas, Lucite.
Mica. A group of natural complex aluminum silicates with highly developed basal cleavage into
thin, tough, flexible laminae. It is probable that if sufficient care were taken it could be split into
thickness approaching molecular dimensions. Owing to the fact that blocks are very expensive, mica
is usually split and punched into parts for capacitors and spacers. For other uses the flakes are cemented
together with adhesives to make "built-up" or "pasted" mica, which forms flexible or rigid sheets, de-
pending on the binder. Flake or dust mica is combined with resins or glasses to form simple molded
shapes as well as rods and sheets. There are several varieties of mica, including:
Biotite — iron mica, black mica Muscovite — potassium mica,
Paragonite — sodium mica common mica
Lepidolite — lithium mica Phlogopite — magnesium mica,
Lepidomelane — iron mica rhombic mica
but only the last two are used for electrical work. Muscovite comes in three colors: white and ruby,
both of which are superior grades, and green, which is inferior electrically and mechanically to clear
grades of white and ruby. Muscovite mica is in general superior electrically and mechanically to
phlogopite, but phlogopite has superior heat resistance. Phlogopite ranges from a deep amber color to
dark amber and milky white. It is not so readily split as muscovite; it is softer, and is lower in mechani-
* Trademark names.
2-40 PROPEBTIES OF MATERIALS
cal strength. Phlogopite mica does not lose water up to temperatures of 800 to 900 deg cent, and some
grades will resist 1200 deg cent without complete disintegration. For this reason it is valuable for
spacing the elements in vacuum tubes and in heating devices. The maximum operating temperature
is best limited to 1000 deg cent, and that of muscovite to 500 deg cent. The power factor and resistivity
of phlogopite are much worse than those of muscovite, although the dielectric strength is nearly the
same. Stained muscovite and all phlogopite are unsuitable for use in capacitors where low power factor
is required. Mica, in general, does not decrease in dielectric strength with frequency as fast as most
dielectrics. This fact, together with its low power loss, enables carefully designed and built mica capac-
itors to operate at extremely high frequencies. The defects occurring in mica are air bubbles, _ stains,
and spots. Mica is graded according to freedom from defects as follows: highest-grade^ mica is clear
and free from all defects; second highest grade has air bubbles between laminae; stained mica sometimes
has some iron stains present; spotted mica is badly stained and usually has inclusions of other minerals.
Mica, splittings are graded for size according to the largest usable rectangular area. For grad-
ing methods, see ASTM D351. The dielectric strength of mica is considerably reduced by air or mois-
ture between the laminae, but the flexibility is somewhat increased. Specifications for block mica and
films: ASTM D748; for electrical tests: ASTM D351.
Mica, Reconstructed or Pasted. Flake mica is bound and pressed together with shellac, gum,
asphalt, or synthetic resin varnishes and milled to thickness to form sheets which may be punched and
sheared. Some grades are flexible and may be formed to a limited extent cold. Others use a thermo-
plastic binder and can be formed to quite intricate shapes at 100 deg cent. Hard grades contain as
little as 3 per cent binder and do not compress appreciably. See also Mica cloth and Mica paper.
Specifications for materials: NEMA Standards 39-55; for testing methods: ASTM D352.
Mica Cloth. A composite insulation of high dielectric strength used for insulating transformers and
field windings.
Mica Paper. Flake mica cemented between sheets of glassine, rice, kraft, or express paper. Mica
also is combined with asbestos paper or fibers to form composite insulations.
Mica Plate. Another name for reconstructed mica sheets.
Micabond.* Continental-Diamond Fibre Co. Reconstructed mica tape, tubes, and sheets.
Micanite.* Mica Insulator Co. Reconstructed mica products.
Micarta.* Westinghouse Electric Corp. Phenolic laminates.
Minerallac.* Minerallae Electric Co. Fusible asphalt compounds.
Molded Compounds. Hot-molded products are formed in. molds or platens heated to a temperature
sufficient to cause the binder to flow, cementing the particles and producing a pure smooth binder
surface which lowers water absorption and increases surface resistivity. Compounds in which binder
hardens under heat are called therm osetting; those in which binder becomes plastic are called thermo-
plastic, and molds must be cooled before the article is removed. Some thermosetting binders are
synthetic resins of the phenol formaldehyde, urea formaldehyde, or melamine type. Some thermo-
plastic binders are shellac, cellulose nitrate and acetate, vinyl resins, mixtures of asphalts and hardened
rosinr copals, casein resins, sulfur chloride phenol resins, cumarin resins, polystyrene, and methacrylate.
Fillers may be either fibrous or powdered, wood flour being the commonest. Cotton, silk flock, or
threads are used to improve resistance to impact, and macerated cloth to give high impact resistance,
with thennosetting compounds. Asbestos is used for heat-resistant products, mica to obtain low
power factor, and ground flint, china clay, silex, stone, etc., to cheapen the article. Compounds can
be hot-molded in great varieties of shapes with thin sections, metallic inserts, threads, etc. Tolerances
can be held to within plus or minus 0.003 in. per in. when not depending on mold closure. Cold-molded
products are formed under pressure and subsequently baked for periods of from a few hours to a week
at temperatures of 150 to 300 deg cent. There is little flow of the binder, and the surface is not very
smooth and depends on the fineness of the filler. Pieces distort slightly in baking, and the accuracy
of dimensions is much lower than in the hot-molded process: it amounts to plus or minus 0.009 to
0.015. Binders are thick varnishes, asphalts, tung and linseed oils, anthracene oils, and various gums
or varnish resins in suitable solvents. Cold-molded compounds are subdivided into refractory and
non-refractory, according to the degree of heat resistance. In general, close tolerance, loose mold
pieces, and threaded parts increase molding cost. For low cost the parts should be designed with
adequate radii, and with no projections, indentations, or holes which require loose pieces in the molds.
Multiform Glass.* Corning Glass Works. Powdered glass, pressed and fired.
Muscovite. Variety of mica suitable for electrical insulation. See Mica.
Mycalex.* Mycalex Corp. Glass-bonded mica, sheet, rod, and molded.
Mycalex,* G. E. General Electric Co. Glass-bonded mica, sheet, rod, and molded.
Mycroy.* Electronic Mechanics, Inc. Glass-bonded mica.
Neoprene. Produced by emulsion polymerization of chloroprene, which is derived from acetylene.
Polychloroprene is the chemical name for neoprene but neoprene generally is used even though it is"
the trade name for the E. I. du Pont de Nemours & Co. product. Neoprene can be vulcanized like
rubber but sulfur is not always required. There are many types of neoprene distinguished by suffix
letters ; some of the types are copolymers with nitriles. Neoprene made in government plants was called
GR-M; freeze-resistant neoprene, FR; general purpose, GN; low oil swelling and low gas diffusion, ILS,
etc. All types are outstanding in oil, ozone, and sunlight resistance and will not support combustion
Neoprene may be compounded to give power factors of 1 per cent and resistivities of 10 12 ohm-cm but
many compounds are poor electrically. Neoprene may also be formulated for high heat resistance or
for good abrasion resistance. One application of great value is the jacket of portable cords and cables
Neoprene also may be made with low specific resistivity for use as electrostatic shields or for potential
control. It also is an excellent gasket material. puwuuai
Nitrocellulose. See Cellulose nitrate.
* Trademark names.
SOLID DIELECTRIC MATERIALS 2-41
Nitron.* Monsanto Chemical Co. Cellulose nitrate.
Nixonite.* Nixon Nitration Works. Cellulose acetate.
Nixonoid.* Nixon Nitration Works. Cellulose nitrate.
Nylon.* E. I. du Pont de Nemours & Co. Polyamide products of all kinds.
Ozokerite. A natural mineral wax, amorphous and black to dark brown. When bleached, it is
white to yellow or brown. Melting point is 70 to 80 deg cent. The purified wax is known as ceresin.
Panelyte.* St. Regis Paper Co. Phenolic laminates.
Paper. Paper for insulating purposes should be as free as possible from all chemicals and from
conducting particles and should be strong mechanically. Paper changes its moisture content very
rapidly with changes of atmospheric humidity. Single sheets of thin paper will come to equilibrium
in as little as 15 minutes, so that all testing, both mechanical and electrical, is done best under condi-
tions of controlled humidity and temperature. The principal types of paper of interest are those fol-
lowing. Rag papers made with a minimum of chemicals and short "cooks" give strong paper with
heat resistance somewhat improved over that of chemical wood papers. Manila papers, made from
manila fiber or from old rope, etc., sometimes with cotton or linen rags, have been the standard cable
papers for some years because of high mechanical and electrical properties. Kraft papers can now be
made, however, with equal or superior properties ; kraft papers properly made are very strong, have
excellent dielectric properties, and are cheaper than rag or manila paper. Glassine or onion-skin paper
is a highly beaten sulfite stock with fair mechanical and electrical properties. It does not take impreg-
nation well, however. High-density, well-beaten, heavily calendered stocks in the thicker sizes are
much used as insulating strips. See Pressboard. Material intermediate between paper and boards in
density or thickness is known by various names — express paper (chemical wood fiber), rope paper
(from old ropes), etc.
Paragutta. Submarine cable insulation compounded of purified gutta hydrocarbon and deresinified
rubber.
Perbunan.* Standard Oil Co. of N. J. Synthetic rubber: a copolymer of butadiene and acrylo-
nitrile.
Petrolatum. Comes in liquid, soft, and hard grades. The soft form is similar to vaseline and is
used extensively as a paper-cable-impregnating material. M.p. 50-55 deg cent. The electrical prop-
erties vary with purity. ^J
Phenol Fiber. General term for paper-base phenolic laminates.
Phenolic Insulating Materials. Obtainable in two principal forms: molded parts; and laminated
sheets, rods, or tubes with paper or fabric base. For molding compounds, the resins are combined
with the desired fillers, either by working on rolls or by coating the filler particles with a varnish and
drying (see discussion of molded compounds). For laminated products, sheets of paper or fabric are
coated or impregnated with varnish and pressed hydraulically between heated platens. Rods are
wound on small mandrels which are removed and the roll is cured in a mold. This leaves a weak center
section, and for some purposes rod turned from sheet stock is preferred, although it does not machine
as well and splits more readily. For molded tubes the impregnated paper is wound on mandrels and
the assembly cured in heated molds. Since the pressure, of course, is not radial unless an expanding
mandrel is used, the seams in molded tubes are weak and tend to split apart. To overcome this, a
rolled tubing is manufactured which is cured by heated rolls during the winding. Since the pressure is
limited in this process, the electrical properties generally are not equal to molded tubing but the me-
chanical properties are superior. Laminated phenolic insulation is hard, tough, and rigid, but more
elastic than equivalent molded compounds. It is infusible and resists temperatures up to 125 deg cent,
but becomes slightly more brittle upon cooling after continuous operations above 90 deg cent, and
usually shrinks somewhat more than it had expanded. A slight softening is noted while the compound
is hot, of which advantage is taken to reduce breakage in punching operations. Stress applied while
hot causes a slight permanent set, and a limited forming is thus possible. The dielectric properties
are not so good as those of hard rubber, but, mechanically, phenolic insulating compounds are superior
and do not corrode metals or deteriorate with age. Specifications for laminates: NEMA Standards,
and ASTM D709; for molding compounds ASTM D700.
Phenolic Resins. Phenol and various other phenolic substances, such as cresol, will condense and
polymerize with aldehydes under the influence of heat and a suitable catalyst. Formaldehyde and
hexamethylene tetramine are the commonest substances employed to react with phenols or cresols.
The reaction is catalyzed by ammonia, alkalies, acids, and other agents. The reaction proceeds in two
or more stages. In the first stage the resin is fusible and soluble in acetone and other solvents. Upon
further heating the resin becomes infusible and practically insoluble. This second stage is the base of
thermosetting molding compounds and of some phenolic laminating or baking varnishes.
Phenolite.* National Vulcanized Fibre Co. Phenolic laminates.
Phlogopite. Variety of mica, q.v.
Piccolastic.* Pennsylvania Industrial Chemical Corp. Substituted styrene polymers.
Plaskon.* Plaskon Div., Libby-Owens-Ford Glass Co. Urea or melamine molding compounds.
Plastacele.* E. I. du Pont de Nemours <fc Co. Cellulose acetate products.
Plax.* Plax Corp. Polystyrene.
Plexiglas.* Rohm and Haas Co. Methyl methacrylate products.
Pliolite.* Goodyear Tire and Rubber Co. Cyclicized rubber thermoplastic resin.
Polectron.* General Aniline & Film Corp. Polyvinyl carbazole resin.
Polyamides. Thermoplastic resins formed from dibasic acids and diamines. Nylon, the most
important, is formed from adipic acid and hexamethylene diamine. It is characterized by extraordinary
strength and toughness, and by a high degree of resistance to solvents and chemicals. The electrical
characteristics of nylon are good but not so outstanding as its mechanical properties. It has been used
* Trademark names.
2-42 PKOPBRTIES OF MATERIALS
successfully for thin-wall coil forms and for thin-wall jacketing of assault wire. Its strength and fungus-
resisting properties have led to its use for many military applications in connection with parachutes,
aircraft, guy, mooring, and tow ropes, cords, etc. It is available as yarn, monofilament, and molding
compound. Yarn and monofilament are cold-drawn or orientated to effect a very considerable increase
in tensile strength. Specifications: ASTM D789.
Polydichlorostyrene. Thermoplastic prepared by polymerization of dichlorostyrene. It is similar in
most respects to polystyrene except that a considerable increase in heat distortion temperature has
been made with only a slight sacrifice in electrical properties. Trade name: Styramic H.T.
Polyethylene. Prepared by the polymerization of ethylene,' polyethylene is outstanding for low
electrical losses at high frequencies and has found extensive application as a dielectric in r-f coaxial
cables. In thin sections it is flexible, but thick sections are rigid and can be machined. It is thermo-
plastic and is fabricated by injection or extrusion. It is available in the forms of molding compound,
tape, tubing, monofilament, and rods or slabs. English practice includes plasticizing with polyiso-
butylene, which lowers the cold-brittleness point. Polyethylene is insoluble in common solvents when
cold but dissolves in hot hydrocarbons. Coatings of polyethylene may be applied by flame-spraying
or by the use of emulsions. Coatings have a low moisture permeability. Trade name: Polythene.
Polyflex.* Plax Corp. Flexible polystyrene sheet.
Polystyrene. Thermoplastic resin produced by polymerization of monomeric styrene with heat and
sometimes a catalyst such as a peroxide. Polystyrene is outstanding for low dielectric loss at high
frequencies. It has high dielectric strength and good arc resistance. It has zero water absorption and
good mechanical strength, and it does not become more brittle at low temperatures. It has exceptional
optical clarity and high refractive index. Unfortunately, it cannot be used at temperatures much above
65 deg cent without cold flow occurring, and some tendency for surface crazing exists. Crazing may be
minimized by suitable heat treatment to remove surface strains. Attempts to increase the operating
temperature by the use of fillers have not been too successful, for they increase the tendency to crack.
The usual method of fabrication is injection molding, although many parts are machined from sheet,
rod, or tube stock. Polystyrene may be drawn or oriented to form a flexible sheet (Potyflex *) or
plasticized to make films for use in capacitors, etc. Specifications : ASTM D703. Trade names : Loalin,
Lustron, Plax, Pdyflex, Styron*
Polystyrene, Modified. Polystyrene has been combined with chlorinated diphenyl to form a non-
inflammable plastic with a heat distortion point somewhat higher than that of polystyrene. It is also
easier to machine, but the electrical losses are slightly higher. Trade name: Styramic. Other modi-
fications are possible, such as copolymerizing styrene with other materials such as butadiene. With
about 25 per cent styrene Buna S rubber is formed, but if the styrene is considerably in excess a semi-
flexible thermoplastic (Styraloy *) is produced. This material has good dielectric properties and is
very tough. It is suitable for wire and cable insulating. Cerex * is another recently introduced styrene
copolymer with improved heat resistance, high strength and hardness, and unusual chemical resistance,
but somewhat higher losses than polystyrene.
Polytetrafluoroethylene. Manufactured by polymerizing gaseous tetrafluoroethylene; a plastic
with remarkable heat, chemical, and solvent resistance. Polytetrafluoroethylene is very tough over a
wide temperature range and has a loss factor less than that of polystyrene; its dielectric constant of
2.0 is the lowest of any solid insulating material. It is very expensive as of 1949, and extrusion or mold-
ing is slow. Some machining is necessary on most parts since molding is very difficult. Trade name:
Teflon^
Polythene.* E. I. du Pont de Nemours & Co. Polyethylene.
Polyvinyl. See Vinyl.
Porcelain. A ceramic body usually composed of clay, feldspar, and flint, finely ground, mixed
with water, formed to desired shape, dried, and fired at temperatures usually ranging from 1300 to
1800 deg cent. When desired, glaze is applied on all surfaces, except the base on which the part rests
in the kiln during firing, by painting on a composition which fuses to a translucent or transparent glass.
Mixtures of china clay or kaolin, which are slightly plastic, and ball clay, which is very plastic, are
used to give the necessary working properties to the wet dough. Feldspar is a naturally occurring
potassium aluminum silicate. Flint is added in the form of ground sand or quartz. Normal por-
celains contain from 20 to 60 per cent of clay, from 15 to 50 per cent of feldspar, and from 0 to 65 per
cent of flint. Magnesia sometimes is added up to 50 per cent to improve the strength at high tempera-
tures. Special porcelains vary widely in composition. Some are made from natural aluminum silicates
such as andalusite with enough clay to give a bond. Magnesium silicate ceramics made with bases of
talc, steatite, etc., give modified porcelains with superior electrical and mechanical properties. The
raw "body" or dough is formed into shape by two distinct processes. In the dry process the mass is
compressed in steel dies. Parts must have "draft" and taper similar to die castings, and a tolerance of
plus or minus 1/64 in. per in. is necessary to allow for shrinkage variation in firing and wear of molds by
abrasion. Minimum commercial tolerance on thickness is plus or minus 0.010 in. Dry-process por-
celain is used for insulation under 5000 volts only, since it is porous and weaker mechanically and
electrically than wet-process porcelain. The porosity is from 3 to 5 times as high as that of wet-process
parts. Wet-process porcelain is made by forming the dough to the approximate shape, drying and
machining on vertical or horizontal lathes to final shape. It also is sometimes cast in a fluid state in
absorbent molds which remove enough water to enable the part to be removed after some time and
dried. Cast porcelain compares favorably with formed wet-process porcelain. Wet-process porcelain
has a very low porosity and high dielectric strength. A tolerance of about l/32 in. per in. , plus or minus
is necessary for commercial manufacture. All porcelain is relatively weak in tensile, flexural and
impact strength. It has poor resistance to thermal shock except in special grades. The mechanical
strength depends upon the flint content, the heat resistance upon the clay, and the dielectric strength
* Trademark names.
SOLID DIELECTRIC MATERIALS 2-43
upon the feldspar, which unfortunately tends to make the parts brittle. Porcelain is comparatively
inexpensive and chemically inert. Dry-process parts are considerably cheaper than wet-process parts.
Glazing improves the resistance to weathering, but it must have a coefficient of expansion similar to
that of the body, for a cracked or "crazed" glaze reduces the strength. The insulation resistance of
normal porcelains drops rapidly above 300 deg cent; to minimize this effect, alkali metals are reduced
in amount as much as possible. For high-temperature work free quartz in the fired body is undesirable
since it has irregularities in its thermal expansion curve which tend to cause cracking, and so it is
eliminated as far as possible. The desirable structure is usually crystals of aluminum silicates (known
as mullite and sillimanite) evenly embedded throughout a glassy matrix. Pores are, of course, highly
undesirable. Fired porcelain parts can be ground to meet <slose tolerances, and two or more subparts
can be fastened together with neat Portland cement, litharge-glycerin cement, or asphalt and resin
base compounds. Low-melting metals, such as babbitt, may be cast around porcelain with some
attendant danger of cracking.
Pressboard. A material similar to paper except that it is thicker, less flexible, and usually denser.
Grades containing above 50 per cent cotton fiber may be formed by heat and pressure into simple
shapes. The better grades" are also known as fullerboard. Pressboard is much used for low-frequency
coil construction with subsequent impregnation. The material, of course, is hygroscopic and must be
treated with oil, wax, varnish, or other compounds to increase dielectric strength and repel moisture.
The impregnated material is a cheap and satisfactory insulator where the highest dielectric properties
are not required.
Prestite.* Westinghouse Electric Corp. Special dry-process porcelain.
Pyralin.* E. I. du Pont de Nemours & Co. Cellulose nitrate.
Pyrex.* Corning Glass Works. Electrical, heat, and chemical resistant glasses.
Pyroxylin. See Cellulose nitrate.
"Q" Max** Communication Products Co. Low-loss r-f coil lacquer,
Quartz, Fused. Silicon dioxide fused at 1750 deg cent to a clear, translucent, glassy mass. Very
stable, will not absorb water, and is an exceptional insulator. Strong mechanically and extremely
resistant to thermal shock on account of the low coefficient of expansion* It is not attacked by solvents
or solutions except by hydrofluoric acid and slowly by concentrated alkalies. For high temperatures it
must be kept clean, as traces of metallic salts or oxides will flux the quartz to form a low-melting glass
and cause failure of the tube or other device. It is available in rods, blocks, tubes, and extruded shapes.
Special shapes can be cast in graphite molds. It can be ground and disk-sawed readily since it does not
•crack easily. It is very expensive.
Rayon. The three common types of rayon are acetate, viscose, and cuprammonium. Viscose
rayon is the strongest and most suitable for protective braids on hook-up wire but is not so resistant to
abrasion as cotton. Viscose rayon contains traces of residual sulfur which may cause corrosion if it is
used for magnet wire insulation; acetate and cuprammonium rayon are suitable for such applications.
Acetate rayon is especially suitable for use with very fine wires for it is non-corrosive even under condi-
tions where electrolysis "would take place.
Resimene.* Monsanto Chemical Co. Melamine molding compounds.
Resinox.* Monsanto Chemical Co. Phenolic molding compounds.
Resistoflex.* Resistoflex Corp. Polyvinyl alcohol products.
Rosin. Rosin is a natural resin obtained by steam distillation of turpentine and rosin oils from
the exudations of certain varieties of pine trees. Rosin comes in letter grades. WW (water white) is
the best, descending in reverse alphabetical order to A and B, which are very impure grades, contain-
ing much dirt, and almost black. It is universally graded by the color. Although the properties do not
vary directly with the color, the color is important for use in varnishes. Rosin in grades from WW to
H is extensively used in oil and wax impregnating compounds. It also is very cheap. Probably the
most important use in the electrical industry is non-corrosive soldering flux. Solutions of rosin in
No. 1 S.D. alcohol, or in alcohol and ethyl acetate, form a substantially non-corrosive soldering flux
and yet the activity of rosin at the temperature of melted solder is sufficient to remove thin coats of
metallic oxides and insure a good joint on tin, copper, brass, or nickel silver. It is unsatisfactory for
steel. Any rosin left around the joint is non-conductive, which is a further advantage.
Rubber, Cyclicized, Thermoplastic resin derived from natural or special synthetic rubber by treat-
ment with stannic chloride or chlorostannic acid. This resin is extremely resistant to moisture diffu-
sion and may be added to wax mixtures to decrease cracking at low temperatures. Trade names:
Pliolite, Marlon B.
Rubber, Hard. Hard rubber is usually vulcanized with 20 to 30 per cent sulfur, in the form of
sheets, rodsT tubes, or molded shapes. It is also called vulcanite and ebonite, and is known under
various trade names. It is a hard, dense material, is easily machinable, takes a high polish, and is
resistant to wear. At temperatures slightly below room temperature it becomes increasingly brittle,
and at higher temperatures it softens and flows under pressure. Under heavy load, "cold flow" occurs
at room temperature. In a small intermediate temperature range it is tough and almost "unbreak-
able." It is combustible but is not easily ignited. It has low water absorption and is immune from,
attack by most acid and alkali solutions and fumes. It is attacked 'and swelled by oils and rubber
solvents. It is attacked by ozone, although less than soft rubber, but special grades are available with,
improved oil and ozone resistance. It is resistant to sparks but will not withstand heavy arcs. The
sulfur is never fully combined, which leads to some serious difficulties. The sulfur has a tendency to
appear in a surface film known as "bloom," causing discoloration. Ultraviolet light produces sulfuric
acid from this layer, seriously lowering the surface resistivity and causing corrosion of nearby metals.
"Blooming" can be greatly reduced by careful compounding. Metallic inserts should be protected by
& coating of tin or other 'corrosion-resistant substance. The tendency to "cold flow" and the high co-
* Trademark names.
2-44 PROPERTIES OF MATERIALS
e^cient of expansion can be reduced by incorporating suitable fillers such as talc; lower grades of hard
rubber usually are filled for economic reasons, however. Rubber can be preformed before molding
to nearly the final shape and hence may be used for fine tubes and thin-walled sections not easily ob-
tainable with phenolic moldings, but the accuracy in molding is usually much lower, owing to shrinkage,
distortion, and high coefficient of expansion. Hard rubber is easily machined by normal methods, but
grinding is sometimes more economical. Special drills also give improved performance, and lubricants
are valuable for drilling, tapping, and turning. Tungsten carbide and diamond tools give more nearly
satisfactory production. The material may be sheared and punched if heated. Many moldings as
well as machined parts require polishing with pumice on a moderately hard "buff" at low speed to
avoid excessive heat. The material usually is black but can be obtained in a number of colors, mostly
with high filler content. Hard rubber has very high dielectric strength and resistivity, and low dielec-
tric constant and power factor, but all the dielectric properties are affected seriously by rising tempera-
ture. The mechanical temperature limit is about 45 deg cent for unloaded and 70 deg cent for loaded
hard rubber with light pressures.
Rubber, Synthetic. The principal synthetic rubbers are Buna S, Buna N, neoprene, butyl, and
Thiokol,* although elastomeric vinyl compounds might also be classed as synthetic rubber. All the
above are discussed elsewhere in this section.
Rubber, Vulcanized. Sulfur and rubber react at temperatures in the vicinity of 100 deg cent to
form a tough, elastic, strong material. The crude rubber is washed, sheeted, and dried. The sheets
are then mixed on hot rolls with sulfur, fillers, plasticizers, accelerators, and anti-oxidants as wished,
and sheeted, molded, or extruded to the desired forms. The article then is vulcanized by heating to
temperatures from 125 to 145 deg cent for soft rubber articles, and 160 to 170 deg cent for hard rubber
parts. With plain rubber, from 2 to 10 per cent sulfur gives a soft rubber stock. Hard rubber contains
from 20 to 32 per cent sulfur. With plain sulfur, vulcanization or "cure" may take 2 or 8 hours, but
by means of accelerators the time may be reduced to as low as 20 minutes. Litharge, lime, and mag-
nesia are inorganic accelerators as well as fillers. Complex organic compounds, such as tetramethyl-
thiuram disulfide, phenylguanidines, and mercaptobenzothiazole, function to give fast cures which are
not critical as to the time required to obtain maximum physical properties and are known as "flat"
cures. Fillers in the form of fine powders, such as carbon black, zinc oxide, clay, and whiting, are em-
ployed in nearly all rubber goods. They cheapen the compound, of course, but they also increase the
strength and toughness. Soft rubber compounds usually contain from 50 to 80 per cent of filler. Al-
though the natural resins and proteins assist in the "milling" or breaking down of the rubber to some
extent, very often improved working is obtained by adding plasticizers or softeners, including paraffin,
waxes, para-cumaron resin, oils, fats, and asphaltic and bituminous materials in various percentages.
Reclaimed rubber also improves the working properties. So-called mineral rubber, which is an asphaltic
residue, is sometimes added up to 20 per cent and can be classed as a filler. The dielectric constant of
rubber-sulfur compounds at 25 deg cent rises from 2 to 11 per cent of sulfur and falls again from 16 to
19 per cent sulfur, and then changes very slightly up to 32 per cent sulfur. The power factor goes
through somewhat similar variation, starting at 8 per cent sulfur. The maxima of these curves are
displaced to higher sulfur content by increasing temperature. The normal soft and hard rubber com-
positions thus have low dielectric constant and power factor, and the intermediate region, which is
seldom used, has poor electrical properties. Resistivity rises in a fairly regular curve from 2 to 28 per
cent sulfur. (See Bureau of Standards Scientific Paper 560, part II, by H. L. Curtis, A. T. McPherson,
and A. H. Scott.) Softeners change the dielectric constant slightly but may seriously increase the
power factor in quantities of only 10 per cent. The dielectric constant is increased nearly propor-
tionally to the filler content. Carbon black causes a sharp increase of dielectric constant from 2.7 to
6.0. Zinc oxide, lead oxide, and selenium show much slower rates of increase. Powdered quartz gives
only a slight increase. The effect on the power factor is much the same: 20 per cent carbon black ele-
vates the power factor from 0.0025 to nearly 0.05. Increasing quartz content slightly improves the
power factor. The introduction of carbon black greatly reducps the resistivity of rubber. Carbon
black is, however, the best filler from a mechanical standpoint: a several-fold increase in the tensile
strength is produced. Rubber compounds absorb water, which causes an increase of dielectric con-
stant and power factor, and decrease of resistivity, but on long immersion the power factor may de-
crease again. Water absorption can be considerably lowered by extended washing of the crude rubber
to remove water-soluble matter and by the use of water-insoluble fillers such as silica, zinc oxide, or
hard rubber dust. Absorption of water is less in sea water than in distilled water. The usual grade of
wire insulation contains 20 per cent minimum of rubber; better grades have 30 per cent, and high grades
40 per cent. Covering of portable cords, etc., subject to mechanical wear may contain up to 60 per
cent. The mechanical and dielectric strength of rubber is lowered by the action of oxygen and more
rapidly by ozone which is present in corona discharge: the rubber cracks when normally vulcanized
and may melt if the temperature is high and the compound is undervulcanized. In order to improve
the resistance to oxygen, organic compounds, such as diphenylamines or hydroquinone, known as
antioxidants, are added in small percentage. Rubber stocks are tested for this defect under 300 Ib
per sq in. in oxygen gas at 70 deg cent and by contact with ozone at atmospheric pressure. Stretching
the rubber under test seriously increases the rate of ozone attack. Ultraviolet light also sharply accel-
erates the combination with oxygen. Heat deteriorates rubber rapidly; 49 deg cent is the maximum
operating temperature for Code rubber insulation. Performance grades are satisfactory at 60 deg cent,
and heat-resistant grades at 75 deg cent. Rubber is swelled quickly and eventually dissolved by hydro-
carbon solvents and oils. Special grades are available which minimize this defect. At low tempera-
tures a low-sulfur rubber compound is no longer elastic, and a piece stretched and cooled to -20 dec
cent or lower will not return to its original length until the temperature rises. The power factor also
increases sharply to a maximum in this region, with a value over 10 times the value at 20 deg cent,
* Trademark names.
SOLID DIELECTKIC MATERIALS 2-45
indicating a change of state in the compound. The power factor also rises with increasing temperature,
but less rapidly.
Rutile (TiO2>. A particular crystalline form of titanium dioxide, with a dielectric constant of 80
to 110, which is used in the manufacture of high-dielectric-constant ceramics.
Saflex.* Monsanto Chemical Co. Polyvinyl butyral.
Saran.* Dow Chemical Co. Vinylidene chloride.
Saturated Sleeving. Cotton sleeving impregnated with thin varnish or compound which does not
fill completely the interstices of the fabric. Dielectric strength is low, and resistance to humidity is
poor. It is valuable mainly to space conductors apart.
Scotch Tape.* Minnesota Mining and Mfg. Co. Pressure-sensitive, non-corrosive electrical tape
with various backing materials.
Shellac. Produced by the insect Tachardia lacca, which attaches itself to numerous species of trees
native to India, Indo-China, and Siam, and excretes the resin at several parts of the 6-month life cycle.
The kusmi tree is the most valuable host to the parasite lac insect since the lac therefrom is of higher
quality. Crude lac consists of about 75 to 85 per cent resin, 2 to 4 per cent dye, 1 to 2 per cent ash,
2 to 3 per cent water, and 9 to 15 per cent residue and dirt. The natives wash the crude lac, dry it, and
press it through a bag with the aid of heat. The mass is plastered into a sheet on a heated object and
stretched while still hot. After it cools it is broken into flakes and shipped in bags. Native shellac is
sometimes adulterated with rosin. Machine-made shellac is extracted by various processes employing
solvents or heat. Refined shellac contains over 90 per cent resin, from 3 to 5 per cent of wax, 1 to 2
per cent moisture, and 1 to 5 per cent of matter insoluble in alcohol. Shellac is sold in many grades
which are principally determined by the color. D.C. is a very high grade, free from dirt. Superfine is
made from best kusmi lac. Fine and Standard No. 1, T.N., and garnet lac follow in descending order
of quality. Rosin is limited by trade standards to 3 per cent maximum except in garnet shellacs which
may sometimes contain 20 per cent. Machine-made shellac is graded somewhat differently. One
manufacturer's grades are Fine, Superfine, and ABTN. All are hard, pure shellacs. BB is used for
blending, and amber where a light color is required. Completing the list are: T.N.S. pure orange shel-
lac, various grades of T.N. shellac, and garnet. Machine-made garnet is low in wax and rosin, and is
valuable for insulating use. Shellac is naturally variable in quality, depending on the source and
methods of collection. A small amount of orpiment (arsenic sulfide) is added to some orange shellac to
lighten the color. Orpiment is insoluble in solvents, but otherwise usually has no beneficial or harmful
effect. Shellac has been used for some time in hot molding compounds, in insulating varnishes, and
as a binder for composite insulations of paper, mica, etc. Various mineral fillers, such as asbestos,
powdered mica, clays, marble, and wood flours, are blended with shellac on rolls in a manner similar to
rubber compounding. The material is sheeted off the rolls, and blanks are cut to size. The preheated
blanks are usually molded in steam-heated molds at about 160 deg cent under hydraulic pressure for
about 1 minute, the dies are then chilled with water, and the piece is removed. Little or no chemical
action takes place. The finish is excellent if the mold surface is polished, but parts can be polished sub-
sequently. Accuracy of molding is about the same as that of phenolic moldings, and the dies are much
the same except for the cooling feature. The moldings have good weather resistance and are fairly
impervious to moisture, but they are somewhat brittle at low temperatures and soften at 75 deg cent.
It is not well known that shellac is somewhat thermosetting under certain circumstances. Long-
continued heating above 100 deg cent will solidify the melted shellac to a tough, horny mass. This
action is accelerated by increased heat and by hexamethylenetetramine, aluminum chloride, urea, and
other agents, and is retarded by alkalies, alkaline salts, aniline, and other substances. (See Bulletin 14,
Indian Lac Research Institute.) Shellac is soluble in alcohols and ketones, and the solutions are used
for varnishes and cements. Shellac loses solubility on standing for long periods of time, and the plas-
ticity is also decreased somewhat. The flexibility of shellac films may be increased by plasticizing with
castor oil or tricresyl phosphate.
Silaneal.* Dow Corning Corp. Silicone treating fluid for ceramics.
Silastic.* Dow Corning Corp. Silicone rubbers.
Silica, Fused. Fused silica is similar to translucent fused quartz in its properties, but it is not made
from as pure a sand and usually contains some iron. It is an excellent insulator.
Silicones. Silicones are a class of organo-silicon compounds with a chemical structure analogous
to that of hydrocarbons, but with the carbon atoms of the chain replaced by silicon atoms with an
oxygen atom inserted in each bond between the silicon atoms. By attaching various hydrocarbon
chains to each silicon atom, and varying the chain length by different polymerization procedures, fluids,
greases, plastics, and resins are produced. The general properties of silicones compared to those of
hydrocarbons are: (1) improved heat resistance; (2) smaller change in viscosity with temperature;
(3) resistance to oxidation; (4) resistance to arcing; (5) high flash and fire points. In common with
some hydrocarbons, they have low power factors and are water-repellent to a high degree. Silicone
fluids are available in viscosities from 0.65 to 1000 centistokes at 25 deg cent, and in volatilities from
nearly zero to approximately that of water. They have dielectric constants of 2.4 to 2.75, and power
factors of 0.0002 from 100 cycles to 10 Me, rising to 0.0006 at 100 Me. Power factor increases with
temperature but is always less than that of a good grade of mineral oil. Silicone fluids may be used to
treat gla^ss or ceramics (Silaneal;* Dri-film *) to produce a gwater-repellent surface, giving a greatly
increased surface resistivity under condensation conditions. Silicone greases (DC No, 4 Ignition Seal-
ing Compound) may be used to fill connectors to prevent arc-over, corona, or leakage, or to render
surfaces water-repellent. Silicone resins are used in conjunction with glass textiles to form heat-
resistant boards, cloths, and wire insulation, and in the form of varnishes for coil impregnation. Sili-
cone rubber (Silastic *) is heat-resistant to 250 deg cent, remains flexible down to —55 deg cent, and
has good dielectric properties.
* Trademark names.
2-46 PROPERTIES OF MATERIALS
Bass, S. L.f and T. A. Kaupp, Proc. I.R.S.< Vol. 33, 441 (July 1945).
Johannson, O. K, and J. J. Torok, Proc. I.R.E., Waves and Electrons section, Vol. 34, 296 (May
1946).
Norton, F. J., Gen. Elec. Rev., August 1944.
Silk. Silk is obtained from cocoons spun from double continuous filaments secreted by the "silk-
worm," which is the larva of the Bombyx mori and other moths. The fiber is unwound from the cocoon
by hand, usually scoured (degummed) to remove the natural sticky gum or wax, called sericin, which
cements the duplex filaments, and twisted into thread. Cultivated silkworms are fed on mulberry
leaves; wild silkworms give a coarser quality known as tussah silk. Orgazine silk is from the best
selected cocoons, and tram silk is from the poorer cocoons. Floss silk is spun from broken lengths of
filaments. Silk for insulation should be free of loading materials and as well washed as^ possible, since
thorough
plain or v
strength ^ UJt — ^.. _„„_ _ „_ __...„.
constant but is not as resistant to heat. Silk flock is sometimes used to add strength to molding
compounds.
Sisal Hemp. A bast cordage fiber obtained from the leaves of the century plant or agave. In
strength and length of fiber it is inferior to manila hemp. It is used to some extent in making paper
and pressboard, and for reinforcing large molded laminated parts.
Spauldite.* Spaulding Fibre Co. Phenolic laminates.
Steatite. Principal ceramic used for radio apparatus. Made chiefly from magnesium silicate
which, after firing, forms clinoenstatite crystals. Low water absorption and excellent electrical prop-
erties are characteristic. Special grades (L-5) are available with even lower losses than standard or
regular grades (L-4 or L-3). Specifications: Joint Army-Navy Spec. JAN-I-10, Grades L-3, L-4, or L-5.
Styraloy.* Dow Chemical Co. Elastomeric polystyrene copolymer.
Styramic.* Monsanto Chemical Co. Polystyrene and chlorinated diphenyl molding compound.
Styramic H. T.* Monsanto Chemical Co. Polydichlorostyrene molding compound.
Styrene. Volatile liquid monomer, also known as vinyl benzene, used for manufacture of poly-
styrene, Buna S rubber, and other plastics. Polymerizes spontaneously in time to polystyrene or
more rapidly with the aid of heat or a catalyst. It also is used as a fully reactive constituent in poly-
ester laminating liquids so that no solvent evaporation is necessary.
Styrofoam.* Dow Chemical Co. Expanded polystyrene.
Styron.* Dow Chemical Co. Polystyrene of various types.
Synthane.* Synthane Corp. Phenolic laminates.
Teflon.* E. I. du Pont de Nemours & Co. Polytetrafltioroethylene products,
Tegit* Garfield Mfg. Co. Asbestos coal-tar moldings.
Tenite I.* Tennessee Eastman Corp. Cellulose acetate.
Tenite IE.* Tennessee Eastman Corp. Cellulose acetate-butyrate.
Textolite.* General Electric Co. Phenolic and other molded or laminated products.
Thalid.* Monsanto Chemical Co. Low-pressure or contact laminating resins.
Thiofcol.* Thiokol Corp. Polysulfide rubbers.
Transite.* Johns-Manville Corp. Portland cement and asbestos molded products.
Tnf-nex.* Libby-Owens-Ford Glass Co. Tempered glass.
Tun.* International Products Corp. Glass-bonded mica.
Urea Resins. Reaction of urea, CO(NH2)2, and formaldehyde produces methylol ureas which are
water-soluble. Paper, alphacellulose, cloth, or wood is impregnated with solutions and cured with
heat and catalysts to a thermosetting, water-insoluble plastic. Urea moldings are light weight, rigid,
and hard. They have high dielectric strength, good arc resistance, and moderate electrical losses.
Impact strength is lower than that of phenolic materials. Translucent moldings in any color may be
obtained. Specifications: ASTM D705. Trade names: Beetle, Plaskon.
Varnishes, Insulating. Varnishes are generally classified according to composition, as oleoresinous
or 4'oil varnishes" and "spirit varnishes," but some commercial types do not fall strictly into either
class. Oil varnishes are made by combining a resin, commonly a copal, with a drying oil. It is usually
necessary to melt or "run" the resin before adding the oil to get a clear solution. Varnishes with a
high oil content are known as "long-oil" varnishes; they are slow drying but deposit very flexible films.
"Short-oil" varnishes have high resin content and deposit a hard film. Oil varnishes harden as a result
of oxidation and polymerization of the drying oils, such as linseed, tung (China wood) , or soya bean,
and often of the resin or asphalt as well. Drying is accelerated by adding small percentages of cata-
lytic agents, called "driers," usually in the form of resinates or linoleates of cobalt, lead, or manganese,
which increase the rate of oxidation. Short-oil varnishes will air-dry in 4 to 18 hr, depending on the
type, to a reasonable degree of hardness. Long-oil varnishes will not air-dry in a reasonable time. By
baking at 100 to 110 deg cent the drying time can be shortened to 2 to 8 hr because of the faster oxida-
tion. Baking produces a harder film and gives better adhesion to the object. It also serves to drive
out moisture from fibrous materials which are being treated, and to improve the dielectric properties.
Many modern insulating varnishes contain synthetic resins of the phenol-aldehyde or alkyd type which
give hard durable films as the result of the thermosetting of the resins during baking. Thermosetting
resins are also used dissolved in "spirit"-type solvents instead of oils, yielding a moderately nard film
on air-drying, which is increased in hardness and durability by baking. The dielectric properties of
the synthetic resin varnishes are usually excellent. Asphalts are used with resins in some black oil
varnishes and without oil or resin in the so-called asphaltum varnishes which are merely solutions of
asphalts in benzine or other hydrocarbons. These varnishes dry principally by evaporation, but the
last traces of solvent leave the asphalt very slowly, and if the object is heated to drive off the solvent
many of the asphalts will oxidize and polymerize to a certain extent, producing a fairly hard film.
* Trademark names.
SOLID DIELECTRIC MATERIALS
2-47
Spirit varnishes dry by evaporation of the solvent, leaving a film of the dissolved resin, asphalt, or
gum. Cellulose nitrate and acetate varnishes are in this class but are usually considered separately
as "lacquers." Many of the resins leave a brittle film when used alone so that a soft gum or plasticiz-
ing agent like castor oil is usually added to give the necessary flexibility, except in shellac which ordi-
narily does not need plasticizing. The principal spirit varnish resins are shellac, manila copal, dammar,
mastic, kauri, and sandarac. The solvents and thinners used are alcohols, esters, hydrocarbons, and
turpentine. Spirit varnishes are commonly air-drying, although the evaporation of the solvent is often,
hastened by moderate heating. Spirit varnishes are generally not used for impregnation but are com-
mon for external coats and for sticking, and for bonding of mica and other materials. For external
coating work, varnishes are applied by spraying, dipping, roller coating, or brushing, depending on the
nature of the work. For impregnation, dried articles are dipped while still hot into a varnish of low
viscosity and low surface tension to insure thorough penetration. Dipping time must be determined for
each article by experiment. A much better impregnation is secured by drying coils in a vacuum and ad-
mitting the varnish to the work container, then "breaking" the vacuum and applying pressure. Impreg-
nated coils should be drained and baked at 100 to 110 deg cent for a period sufficient to harden the
varnish film. Higher temperature tends to disintegrate fibrous materials in prolonged baking, and
lower temperatures do not remove moisture. For short drying schedules, temperatures up to 150 deg
cent are sometimes employed satisfactorily. Objects should be exposed to fresh currents of air during
drying in order to remove solvent vapors which retard hardening. For methods of testing dielectric
strength, heat endurance, and oil proofness, see ASTM D115.
Varnished Cloth. A suitable fabric coated with yellow or black insulating varnish so that the
fibers are thoroughly impregnated. Varnished silk usually is from 0.003 to 0.005 in. and cotton from
0.005 to 0.040 in. thick. Tensile strength of cotton-base cloth per inch width of warp runs from 45 to
100 Ib, and Elmendorf tearing strength across the warp varies from 100 to 300 grams. Dielectric
strength usually runs from 800 to 1500 volts per mil.
Varnished Tubing. Commonly called "spaghetti," magneto tubing, etc., according to manufacturer
and grade; made by coating, or impregnating and coating, cotton sleeving with varnishes. ASTM
Specification D372 distinguishes three grades (see specification for details). Grade A is generally known
as flexible varnished tubing, or motor and transformer tubing, or impregnated magneto tubing; it has
a minimum dielectric strength of 7000 volts average. Grade B, generally known as "radio spaghetti,"
has a minimum average dielectric strength of 4000 volts. Grade C is similar to saturated sleeving, and
its dielectric strength is lower.
Vibrin.* Naugatuck Chemical Co., Div. U. S. Rubber Co. Liquid polyesters and cross-linking
monomers.
Vinyl Plastics. An extremely important class of thermoplastic resins, composed of linear chains
formed by the polymerization of monomers of the general type
tinuous chain
If group X is
hydrogen
hydrogen
chlorine
hydrogen
hydrogen
hydrogen
hydrogen
The result is a con-
and group Y is
the product is
hydrogen
chlorine
chlorine
hydroxy ( — OH)
phenyl (CeHs— )
carbazyl (C^HsN — )
acetoxy (CH3-CO-0— )
polyethylene (Polythene *)
polyvinyl chloride (Geon *)
polyvinylidene chloride (Saran *)
polyvinyl alcohol
polystyrene
polyvinyl carbazole (Polectron *)
polyvinyl acetate
methyl (CH3) methylcarboxy (CH30-OC— ) methyl methacrylate (Plexiglas* Lucite*)
If mixtures of two monomers are copolymerized, a copolymer such as polyvinyl chloride-acetate is
produced in which all the Y's are hydrogen, most of the X's are chlorine, and the remainder of the X's
are the acetoxy group. The polyvinyl formals are a general group of polymers with modified chains
constructed like this: (etc.— CH2— CH— CHs— CH-etc.)
A A
If group Z J8
hydrogen
methyl (CH3— )
butyl (C3Hr- )
the product is
polyvinyl formal (Formex,* Formvar *)
polyvinyl acetal (Alvar *)
polyvinyl butyral (Butacite* Butvar^* Saflex,* Vinylite* X)
Of course, different conditions of temperature, pressure, catalyst, and carrier solvent or emulsion, are
required for each case, and the length of the chain of molecules is varied to suit requirements by altering
these conditions. Only those plastics with vinyl in the product name are usually classed as vinyl plas-
tics, but by this illustration the relationship of many of the thermoplastics is immediately apparent.
Vinyl Chloride. Perhaps the most important vinyl plastic from a tonnage viewpoint, vinyl chloride
is very extensively used for hook-up wire insulation, cable jackets, insulating tubing, and tape. It is
* Trademark names .
2-48 PROPERTIES OF MATERIALS
also employed for non-rigid or elastomeric molded parts since it has rubberlike characteristics when
of plasticizer, but, in general, these resins have a rather high dielectric loss and a lower insulation re-
sistance than those of rubber compounds, although they have a high dielectric strength. Wire insulation
for operating temperatures of 80 deg cent is now available, although 60 deg cent has been the limiting
temperature for most older compositions. These compounds are nearly non-inflammable and do not
oxidize like rubber but are subject to some stiffening due to loss of plasticizer with time. Except for
flexing at low temperature the life should be very long. Specifications for resin: ASTM D72S. Trade
names: Flamenol, Geon 100 series, Vinylite Q series, Koroseal.
Vinyl Chloride-acetate. This resin is similar to straight polyvinyl chloride resin except that about
5 per cent of the resin may be vinyl acetate, which improves the processing and extrusion characteristics
and reduces the amount of plasticizer required. "Uses and characteristics are similar to those of poly-
vinyl chloride, but in addition these resins are used for rigid, transparent, or colored sheets of high
dimensional stability and good electrical properties. These resins also have proved to be very success-
ful for high-quality phonograph records and for manufacture of textiles (Vinyori). Specifications for
rigid sheet: ASTM D708; for non-rigid resin: ASTM D742. Trade names- Vinylite V series.
Vinylidene Chloride. Similar to vinyl chloride resins but contains more chlorine, is harder, and is
capable of orientation by drawing or other cold work to increase the tensile strength. ^For molding
purposes, it is commonly copolymerized with 10 per cent of vinyl chloride to serve as an internal plas-
ticizer. Though the electrical properties are not outstanding, the strength, toughness, and non-inflam-
mability of this plastic have made it valuable for fungus-resistant cable braids and ropes, as tubing for
water cooling, etc. Specifications for molding compounds: ASTM D729. Trade name: Saran.
Vinylite.* Carbide and Carbon Chemical Co. Vinyl resins, of which various grades are distin-
guished by suffix letters.
Vinyon.* Carbide and Carbon Chemical Co. Polyvinyl chloride-acetate textiles.
Vistanex.* Standard Oil Co. of N. J. Polyisobutylene.
Vitreosil.* Thermal Syndicate, Inc. Fused silica.
Voltron.* Industrial Synthetics Corp. Vinyl tubing and tape.
Vulcabeston.* Johns-Manville Corp. Asbestos with rubber or gum binder.
Vulcoid.* Continental-Diamond Fibre Co. Resin-impregnated vulcanized fiber.
Vycor.* Corning Glass Works. High-silica glass*
Waxes. Waxes are of three origins: animal, vegetable, or mineral. The principal animal waxes
are: beeswax, m.p. 63 deg cent; wool wax, m.p. 35 deg cent; spermaceti, m.p. 49 deg cent; insect or
Chinese wax, m.p. 81 deg cent. The principal vegetable waxes are: carnauba, m.p. 85 deg cent, and
candelilla, m.p. 68 deg cent. The principal mineral waxes are: montan, m.p. 72 deg cent; ozokerite
refined to form ceresin, m.p. 65-73 deg cent; paraffin waxes obtained from petroleum. Waxes in
general are not "wetted" by water and are very resistant to penetration by moisture. Ceresin and
non-crystallizable high-melting-point paraffin waxes such as Superla,* Syncera,* and Cerese wax * have
higher insulation and moisture resistance than the low-melting paraffins and the animal and vegetable
waxes. Waxes which crystallize, such as montan, have a tendency to crack and admit moisture by
capillary action; mixture with a soft wax or resin usually minimizes this tendency. Wax compounds
are hardened and the flow point raised by incorporating rosin or other resins and higher-melting waxes
such as ceresin, montan, or carnauba. Most naturally occurring waxes have low dielectric constants
and low power factors as well as high resistivity. Synthetic waxes made by chlorinating naphthalene
or paraffin have somewhat higher dielectric constants and losses. Long heating of liquid waxes at
high temperatures in contact with air tends to cause decomposition and development of acidity, par-
ticularly in the presence of copper, which acts as a catalytic agent to increase oxidation markedly.
Zircon Porcelain. This material consists chiefly of zirconium silicate with addition of small amounts
of clay and metallic oxides to aid in manufacture. It has higher mechanical strength than other
electrical ceramics, and a lower coefficient of expansion than all but cordierite. It is extremely re-
sistant to thermal shock. The electrical characteristics at radio frequencies are excellent, except that
the dielectric constant is 50 per cent higher than that of steatite and changes more rapidly with tem-
perature. The resistivity at high temperatures is about the same as that of steatite and is superior
to that of cordierite and high-voltage porcelain.
6. LIQUID DIELECTRICS
Dielectric Constant. The dielectric constant of liquids ranges from about 1.5 to almost
100. Non-polar liquids at room temperature have constants of 1.84 to 2.3, which are
nearly equal to the square of the index of refraction. The dielectric constants of non-polar
liquids are independent of frequency and vary only slightly with temperature, owing to
thermal expansion. On the other hand, polar liquids have higher dielectric constants
which vary to a marked degree with temperature and frequency in certain regions When
a polar liquid freezes, part of the influence of the dipoles is lost and the dielectric constant
drops very sharply. High rates of change in dielectric constant with frequency or tempera-
ture are normally associated with high power factors at the same frequency and tempera-
ture. The dielectric constants and dipole moments of some liquids are shown in Table 2.
* Trademark names.
LIQUID DIELECTRICS
2-49
Table 2. Dielectric Properties of Liquids
Substance
Temper-
ature,
deg
cent
Wave-
length ,
cm
Dielectric
Constant
(X)
Temper-
ature
Coeffi-
cient of K,
io~4/°c
(negative)
Polar
Moment,
io-18
esu
Conductivity,
mhos /cm
Acetone
-80
oo
33.8
0
oo
26 6
«
+ 15
1200
21 85
a
17
73
20 7
a
25
00
21 3
2 75
6 X 10~8
Air (liquid)
- 191
00
1 43
0
Amyl acetate . •
19
oo
4 81
24
1 91
\rnyl alcohol
20
00
16 0
1 7
18
200
10 8
« tt
18
73
4 7
Aniline
18
00
7.32
35
1 56
2 4 X 10~~8
Benzene
20
00
2 282
8 6
o
7 6 X 10~~18
7i-Butyl alcohol
20
oo
17 4
76
1 65
Butyl stearate
25
oo
3.3
Carbon dioxide (liquid)
Carbon tetrachloride
-5
20
00
00
1.60
2 3
12 5
0
0
4 X 10~18
Castor oil
00
4.67
107
+
1 7 x 10~u
Chlorinated diphenyl
mobile . .
25
5.8
163
viscous
25
oo
5.05
133
Chlorobenzene
20
oo
5 72
31 0
1 56
Chloroform.
20
00
4.84
39 0
1 1
<2 X 10~8
Cumene
22
00
2.2
0 4
Cyclohexane
20
00
2 41
8 6
o
Cymene
22
00
2 5
?
<2 X 10~8
Decahydronaphthfliene
20
00
2 26
6 6
o
Decane
20
00
1.991
6.7
0
Decylene
17
oo
2 21 1
o-Dichlorobenzene
wi-Dichlorobenzene .
20
20
oo
OO
10.2
5 11
45
28 0
2.25
1 48
-
Dodecane
20
00
2 017
7 4
o
Ethyl abietate
20
09
3.95
ca. 20
+
Ethyl acetate
20
6 15
1 85
< 1 X 1 0~ 9
Ethyl alcohol . .
Frozen
00
2 7
-120
00
54.6
u it
-80
oo
44 3
ti u
— 40
00
35 3
u st
0
00
28.4
u u
+20
OO
25 8
63 0
1 68
1 3 x 10~9
it u
17
200
24.4
U il
17
75
23 0
U It
17
53
20.6
it It
17
* 4
8 8
u tt
17
0.4
5 0
Ethyl benzene
22
00
2 2
0 5
Ethyl ether
20
00
4.4
46
1 15
<4 X 10~18
Ethylene glycol
20
00
38 8
2 28
3 X IO"7
Glycerin ...
25
oo
43 0
ca 52
+
6 4 X 10~"8
15
1200
56.2
+
u
15
200
39 i
te
15
75
25 4
tc
8.5
4.4
_
1C
0 4
2 6
Heptane
20
00
1 926
8 6
o
4 X 10~13
Hexane ...
20
00
1 890
9 0
o
4 X 10~18
Hydrog^Tx (1 in uid)
— 258 4
00
1 241
o
"Kerosene . ,
25
ca 2 1
?
<1 7 X 10~8
3Vtesitylene
22
oo
2 2
o
Methyl alcohol
Frozen
00
3 07
— 100
00
58 0
« «
— 50
00
45 3
« «
0
oo
35.0
_
tt n
+20
00
31.2
57
1 68
4 4 X 10~~7
Mineral oil
20
00
2. 191
4.7
0
1 X 10~16
2-50
PROPERTIES OF MATERIALS
Table 2. Dielectric Properties of Liquids — Continued
Substance
Temper-
ature,
deg
cent
Wave-
length,
cm
Dielectric
Constant
TO
Temper-
ature
Coeffi-
cient of K,
icrV0c
(negative)
Polar
Moment,
io-18
esu
Conductivity,
mhos/cm
Nitrobenzene
-30
00
3.1
—
_
u
-13
co
3.2
—
—
a
^
CO
3.4
—
—
u
-4
00
3.8
—
—
u
+ 15
00
37.8
—
—
u
18
co
36.45
3.9
2 X 10^8
u
30
00
35.1
_
—
Nitrogen Qiquid) »
-208
00
1.44
_
0
—
Octane .
20
00
1.949
7.6
0
—
20
00
3.11
36
_
2 X 10~13
Peanut oil . «
11.4
00
3.03
—
—
Pentane . ,
20
00
1.845
9.6
0
<2 X 10~10
Petroleum
2000
2.13
_
_
3 X 10~13
Petroleum etner . .
20
00
1.92
_
0
—
Phenol
45
oo
10.3
_
1.73
< 1 . 7 X 1 0~8
•w-Propyl alcohol
20
00
22.2
53
1.66
5 X IO-8
Pyridine . .... .*....
22
00
13.9
2.1
5.3 X 10~8
Quinoline
22
00
9.0
_
2.25
2.2 X 10~8
Rosin oil
20
00
2.55-2.8
ca. 22
—
—
Silicone fluids
DC 200t 200 centistokes..
DC 500, 20 eentistokes...
Toluene
20
20
-83
00
oo
oo
2.76
2.71
2.51
34
31
0
0
,0-H
]0-14
+ 16
00
2.33
_
_
_
it
19
73
2.31
9.8
0.52
<i x io-14
Turpentine
20
00
2.23
2 X 10~13
18
00
2.376
8.2
0.4
<1 X 10~15
17
73
2.37
_
p-Xylene
20
00
2.25
0
_
Water (pure), frozen ,
— 18
5000
3.16
_
_
_
ij
1200
2.85
1.6X 10~*
liquid
+ 17
200
80.6
17
74
81.7
u
17
38
83.6
_
a
18
00
81.07
4 X 10~8
«
50
_
-
1.7X 10~7
Notes. A wavelength greater than 10,000 cm is denoted by °° .
Zero indicates that substance has no polar moment.
Plus sign indicates that substance is polar but value for polar moment was not available.
D-c Conductivity and Resistivity. The d-c conductivity of liquids is ionic in nature
and has a high positive temperature coefficient. Change in conductivity with temperature
is expressed by
0 = G0ea/T or G = GQebt
where £0, a, and & are constants, T is the absolute temperature, and t is the temperature in
degrees centigrade for small temperature differences. Thus a plot of the logarithm of
either conductance or resistivity against I/ T is a straight line, and against t is approxi-
mately straight for small temperature intervals. The increase in conductivity with
temperature is the result of an increase in ionic mobility arising from the reduction in
viscosity. Log resistance-temperature curves therefore change slope at regions where the
viscosity varies sharply, as at freezing or transition points.
The conductivity of pure liquids may be increased enormously by small amounts of
impurities or moisture which readily ionize in the particular liquid. Fortunately the
degree of ionization is a function of the dielectric constant, so that the non-polar liquids
having a low dielectric constant are less sensitive to impurities, especially in low concen-
tration. The difficulty of preventing contamination of liquids of higher dielectric constant
has effectively prevented their use for capacitors. The resistivities characteristic of com-
mercially pure liquids are approximately in inverse relationship to the dielectric constants,
LIQUID DIELECTRICS
2-51
as is shown by the following table taken from The Properties of Dielectrics, by F. M.
Clark, in the J. Franklin Inst.t Vol. 208, 17 (July 1929).
Table 3. Relation between Dielectric Constant and Resistivity
Material
Dielec-
tric
Con-
stant
Characteristic
Resistivity,
ohm-cm
Material
Dielec-
tric
Con-
stant
Characteristic
Resistivity,
ohm-cm
Benzene
Petroleum oils . .
2.15
2.2
4.7 X 1012
10.0 X 1012 (100° C)
China wood oil ...
Castor oil
3.5
4.3
0.08 X 1012 (100° C)
0.06 X 1012 "
Paraffin wax . . .
Cottonseed oil. .
Asphalt
2.25
2.9
3. 1
5.0 X I012
0.2 X 1012
1.0 X 1012 "
Ethyl alcohol
Methyl alcohol . . .
Water
25.0
31.0
81 07
0.3 X 106 (18° C)
0.14 X 106
0 5 X 106
Linseed oil
3.3
0.61 X 1012 "
At very high voltage gradients, some evidence of a saturation range similar to that of
gases has been obtained. With long applications of voltage, impure liquids undergo a so-
called electric cleaning. This is due to a very low rate of ion production so that all ions
are swept to the electrodes and the conductivity drops nearly to that of a pure liquid.
Solid phases also are removed in some cases by cataphoresis, but the breakdown strength
is usually affected to a greater extent than the conductivity.
Dielectric Absorption and Losses. Liquids exhibit some of the phenomena of dielec-
tric absorption shown by solids, but the rate of decrease of the initial current with time is
much faster and normally is detectable only with an oscillograph. The characteristic
"bound charge" of solids also is absent: the discharge current shows practically no evi-
dence of absorption, except in highly viscous liquids of a mixed nature.
The initial high current is reduced, owing to the accumulation of space charges in front
of the electrodes. The resultant non-linear potential distribution can be measured with
probes; or porous cells can be used to remove the space charges from the liquid for meas-
urement. Although the absorption results in a higher a-c conductivity, the effect is of
much smaller magnitude than that in solids, and the a-c losses are much lower. The non-
existence of any discharge phenomena has been attributed to the absorption of space
charges by part of the electrode charges.
The power factor of most commercial non-polar insulating liquids is low, ranging from
0.0001 to 0.01. The power factor at 60 cycles is influenced by the d-c conductivity and
may be expected to double for each 10 to 20 deg cent rise in temperature. At high fre-
quencies, little change in power factor with temperature is to be expected with true non-
polar dielectrics. Many mineral oils have some polar impurities which produce character-
istic peaks in the power-factor curves at frequencies or temperatures where rapid changes
in dielectric constant are occurring.
For an excellent summary of the effects to be expected in polar substances, consult
Dielectric Properties of Organic Compounds, by S. 0. Morgan and W. A. Yager, Industrial
and Engineering Chemistry, Vol. 32, 1519 (November 1940).
Dielectric Strength. Breakdown in liquids, like that in gases, is not permanent, nor
is the subsequent breakdown voltage necessarily reduced. Discussion of breakdown must
be considered for two cases: pure liquids containing no dissolved or suspended gas, solid,
or foreign liquid; and impure liquids.
Breakdown in pure liquids probably occurs by an ionization process similar to that in
gases and undoubtedly is aided by intense voltage gradients built up by space charges
near the electrodes. Change in pressure has practically no effect, but increase in tem-
perature decreases the breakdown strength, particularly when the boiling point is ap-
proached. The time involved in the breakdown process may be as short as 10 ~7 sec with
sufficient overvoltage
Impure liquids usually break down at much lower voltages for a variety of reasons, the
most important of which is the presence of moisture or gases. The electric field tends to
liberate dissolved gases, and, since the gas dielectric strength is only about one-tenth that
of the liquid, the gas ionizes and starts the discharge. The harmful effects of moisture
and gases are greatly increased by fibers or other suspended solid particles which absorb
the impurity. Fibers, particles, or foreign liquids may form "bridges" or "chains" if the
dielectric constant is higher than that of the liquid. Sometimes these bridges lead only
to preliminary or "pilot" sparks which exert no effect on the breakdown. A very small
percentage of impurity usually produces a marked lowering of breakdown strength, but
larger percentages have only a slightly greater effect. Particles of carbon formed by arcs
or sparks give but a small decrease, which is proportional to the concentration.
2-52
PROPERTIES OF MATERIALS
Although the breakdown voltage of pure liquids is linear with distance in uniform
fields, that of impure liquids is considerably influenced by gap geometry. A horizontal
gap gives lower breakdowns with impure oils than a vertical gap because of the difference
in the ease of gas elimination. Small gaps are quite liable to breakdown by fiber bridges;
long needle gaps are scarcely affected by most impurities. Increased gap area obviously
results in lower average breakdown with impure liquids. m
The effect of temperature on breakdown of impure liquids depends on the kind of
impurity. Materials of low dielectric constant are more readily expelled from the neld
as the viscosity is reduced by raising the temperature, but the conductivity of the liquid
is increased. Moisture may be expelled, raising the breakdown. Pressure increases the
dielectric strength by preventing gas elimination or vaporization of the liquid. ^
Since formation of fiber bridges and gas elimination take an appreciable time, the
strength of liquids to transient voltages is little influenced by these impurities. With
steady-state currents, the strength increases slightly as the frequency increases up to
1000 cycles, but may be as low as 30 per cent of the 60-cycle value at radio frequencies,
probably on account of the heating effect.
Commercial Oils. For service in which the liquid will be in contact with air, the use
of mineral oil has been practically universal because of its stable nature and low cost.
Since the breakdown of all oils is approximately 30 to 40 kv rms in a standard 0.1-in. gap
between l-in.-diameter disks, little is to be gained by substituting other oils except a
higher dielectric constant, which is obtained at the cost of lower resistivity. For hermet-
ically sealed applications, such as capacitors, purified castor oil, with a constant of 4.7, is
often used. Carefully purified, chlorinated hydrocarbons, such as "Pyranol," with^a
constant of 4.5, are also employed for this purpose and have an effective advantage in
being explosion-proof.
Mineral oils must be carefully purified to remove unsaturated compounds which cause
accelerated oxidation in service, resulting in low resistivity, low dielectric strength, high
power factor, and the rapid development of sludge. Too drastic a purification, however,
removes naturally occurring antioxidants in the oil, and stability is decreased. The oxida-
tion of transformer oils may be avoided by the use of oxygen-free atmospheres above the
oils as in the "Inertaire" system.
Filtration through diatomaceous earth is effective in increasing the resistivity of many
liquids. Filtration through hard papers is commonly used for purifying and drying oils in
transformer service. Oil should be filtered when the dielectric strength in the standard
0.1-in. gap drops below 22 kv rms. A good oil will show 30 to 50 kv rms. Low-viscosity
oils seem to have the highest dielectric strength, although the flash and fire points usually
are lower.
Testing methods for electrical insulating oils have been standardized by the American
Society for Testing Materials; see ASTM D117. Typical properties for commercial oils
are shown in Table 4.
Table 4. Properties of Commercial Oils
Property
Mineral
Trans-
former Oil
Mineral
Capacitor
Oil
Castor
Oil
Density, average
0.87
0.91
0.96
Viscosity at 37.8° C (100° F), in Saybolt seconds, average
Flash, point/, in d^g ofint, minimum
57
133
100
149
1400
Fire point-, in d^g nfint, minim trm -...-. -.,,...,
148
170
-40
-40
-15
Neutralization number, in rag KOH per gram, maximum
0.03
2.2
0.03
2 2
2.0
4 7
Power factor, at 100° C and 1000 cycles
0 0025 max
0 01
Resistivity, ohm-cm, at 100° C
4 X 1011
>5 X 1012
6 6 X 10l°
Dielectric strength, at 25° C, in kv, minimum
30
30
28
Coefficient of expansion per deg cent
6.3 X 10~4
6 3 X 10~4
Thermal conductivity, in cal per sec per cm per deg cent
3 X 10~4
4.3 X 10~4
Synthetic Liquids. Synthetic insulating liquids of the non-inflammable type are
known as askarels, and a draft of proposed testing methods has been published in the
Proceedings of the American Society for Testing Materials, Vol. 43, 353. These liquids
consist of mixtures of various chlorinated diphenyls and tri- or dichlorobenzene so ad-
justed that the pour point is reduced below service temperatures. The dielectric constant
is about 4.2. Viscosity at 100 deg fahr is about the same as that of mineral transformer
oils. Dielectric strength is slightly higher, and the fact that the liquids are non-inn am-
GASES AS DIELECTRICS
2-53
mable permits the use of large transformers without fireproof vaults. On account of the
non-explosive nature of the liquid, the air space above it may be sealed from the atmos-
phere with a safety diaphragm designed to relieve pressure if a fault occurs. Improved
stability to oxidation and sludging is another advantage of these liquids. Trade names:
Pyranol, Inerteen.
Silicones. Silicons fluids are a recent development and are expensive (as of 1949),
but they appear to be most promising as an insulating medium. Silicone liquids consist
of chains of alternate silicon and oxygen atoms with various organic groups attached in
pairs to the silicon atoms. Those with two methyl groups attached are dimethyl silicones
(Dow-Corning DC 200 fluids). The viscosity increases with the chain length. These
fluids are suitable for use from —40 deg fahr to 400 deg fahr. Another series (DC 500
fluids) is serviceable from — 70 deg fahr to 200 deg fahr. The general advantages of sili-
cone fluids are:
1. Low temperature- viscosity slopes.
2. High flash and fire points.
3. Low volatility and negligible vapor pressure.
4. High resistance to oxidation and heat.
5. Lack of color, odor, or toxicity.
6. Low power factor over a wide frequency range.
7. Non-corrosive to metals and non-solvent for rubber and plastics.
The characteristics of these fluids are shown in Table 5.
Table 5. Properties of Some Liquid Silicones (Dow Corning)
Fluid
Type
Viscosity
Grade,
centi-
stokes at
Viscosity
Temperature
Coefficient
/ . ^210° F \
Freezing
Point,
deg cent
Boiling
Point,
deg cent
Flash
Point,
deg
cent
Specific
Gravity
25° C/25° C
Coefficient
of Thermal
Expansion
Refrac-
tive
Index
at
25° C
V FiOO° F /
min
Unit = 10 3/°C
25° C
DC 500
1.0
0.37
-86
j 52760 mm
37.8
0.818
1.451
.3822
3.0
.51
-70
ca. 800.5 mm
107
.896
1.170
.394
10.0
.57
-67
>20QQ-5 mm
176
.940
1.035
.399
50.0
.59
-55
> 2500-5 mm
282
.955
1.00
.402
DC 200
100
.60
See Note 1
See Note 2
315
.968
0.969
.4030
350
.62
«
«
329
.972
0.966
.4032
1000
.62
"
"
337
.973
0.963
.4035
Note 1. Recommended for use above —40 deg cent.
Note 2. Less than 2 per cent volatile during 48 hours at 200 deg cent.
Electrical Properties of DC 200 Fluids at 25 Deg Cent and 50 Per Cent
Relative Humidity
Frequency,
cycles per sec
Dielectric
Constant
Power
Factor
103
106
108
2.85
2.83
2.81
0.001
.002
.006
Dielectric strength, 250-300 volts per mil
Volume resistivity, 1 X 10U ohm-cm
7. GASES AS DIELECTRICS
Dielectric Constant. The dielectric constants of gases are close to unity and nearly
independent of frequency. The change in dielectric constant of dry non-polar gases with
temperature or pressure is slight and may be calculated approximately from the equation
K- 1 = A X
P
273 -f t
where A is a constant (2.12 X 10~4 for air).
p is the pressure in millimeters of mercury.
t is the temperature in degrees centigrade.
2-54
PKOPERTIES OF MATERIALS
Table 6. Dielectric Constant of Gases
Gas
Temperature,
deg cent
Pressure,
atmospheres
Dielectric;
Constant
Observer
Air
0
1
.000590
Boltzmann 1875
19
20
.0108
Tangl 1907
u
40
.0218
u tt
u
60
.0330
" "
u
80
.0439
It (C
a
100
.0548
a a
23
.000530
Braunmuhl 1927
G&.rbon dioxide
0
1
.000985
Klemencic
15
10
.008
Linde 1895
u u
20
.020
a u
u u
40
.060
" "
Carbon monoxide
Ethylene
0
0
.000690
.0031
Boltzmann
Hydrogen
0
.000264
"
Methane
0
.000944
«
0
.00061
Oxygen
0
.00055
Conductivity and lonization. The conductivity of gases at low potential gradients is
negligible in the absence of ionizing radiation, such as ultraviolet light or X-rays. If a
sufficient voltage gradient exists, all tbe ions are drawn to the electrodes as fast as they are
produced and the very small ion current is constant over a considerable range of gradient.
Increasing the gradient beyond this saturation range accelerates the negative ions (or
electrons) to a velocity which is sufficient to expel electrons from neutral gas molecules at
each collision.
If the number of ions liberated by the collisions exceeds the number of negative ions
which are lost by recombination to form neutral molecules and by diffusion out of the field,
the collision process is cumulative and the current increases continuously to breakdown.
If the electric field is uniform, sparkover will occur, but if the high voltage gradients are
confined to a small region, such as the vicinity of a pointed electrode, a local discharge,
known as corona, occurs. Local discharges produce visible and ultraviolet light which is
effective in increasing ionization throughout the field. This internal photo-ionization
causes extremely rapid breakdowns of air gaps at sufficiently large voltage gradients.
Corona. The production of a corona discharge requires a considerable current which is
carried by ions of lower velocity in the dark regions of the field. A significant power loss
may occur if the corona becomes appreciable. Corona is objectionable because it causes
radio-frequency interference and produces ozone if oxygen is present. Ozone and the
ultraviolet light from the discharge cause rapid deterioration of many solid dielectric
materials, especially of rubber. Corona is normally prevented by operation at reduced
voltages or by the use of suitable corona shields which are designed to produce a more
nearly uniform voltage gradient throughout the air space.
Dielectric Strength and Sparkover. Dielectric strength is the maximum potential
gradient at the instant of sparkover or at the onset of corona. The gradient is determined
by the geometry and spacing of the electrodes. Dielectric strength is influenced by the
nature and purity of the gas, by the density of the gas, and to a lesser degree by the elec-
trode material. When the mean free ion path between collisions is lengthened by lowering
the gas density, the critical terminal velocity necessary for ionization by collision is at-
tained with a lower potential gradient. The reduction in dielectric strength with decreas-
ing density continues until the number of atoms between the electrodes is so small that
very few collisions occur. If the density is still further reduced and the electric field is
Ta-Ki TT TUT- • e i • Tk * xi i non-uniform, the sparkover will occur
Table 7. ICuumnm Sparking PotentuHs over some path ^ than ^ short.
est distance between electrodes. If
the field is uniform, the sparkover
voltage will increase as the density
decreases to very low values, until, in
a high vacuum, gradients as high as
6000 kv per cm may be obtained. The
. minimum in the sparkover voltage is
independent of electrode spacing for uniform fields and depends solely on the nature and
purity of the gas and on the electrode material. A typical set of values for various gases is
shown in Table 7.
Gas
Volts
(d-o)
Gas
Volts
(d-c)
Air
341
Hydro ge n
278
Carbon dioxide . .
Helium
419
261
Nitrogen
Oxygen
251
455
GASES AS DIELECTRICS
2-55
Sparkover voltage in uniform fields is a nearly linear function of the product of gas
density and electrode spacing (Paschen's law).
An empirical equation which reproduces the entire sparkover curve in air for uniform
fields, including the region around the minimum sparking potential, is
V =
293
273 +t
3.000 + loge
+ 300 volts (crest)
where p is the pressure in millimeters of mercury,
S is the electrode spacing in centimeters.
t is the temperature in degrees centigrade.
The calculation of the sparkover voltage for non-uniform fields is not simple; see P. W.
Peek, Dielectric Phenomena in High Voltage Engineering, McGraw-Hill (1929) for extensive
formulas and tables for this purpose. At spacings of the order of one-half the sphere radius,
the sparkover voltage of a gap between equal spheres is slightly higher than for a uniform
field, but as the ratio of spacing to radius increases the sparkover voltage becomes much
less than for a uniform field. At ratios above 2, corona occurs before sparkover, but
corona is not easily detected at 60 cycles until the ratio is about 8. Representative spark-
over voltages for sphere gaps are shown in Table 8.
Table 8. Sparkover Voltage in Rms Kilovolts
Barometer 76 cm, temperature 25 deg cent
Diameter of Spheres
Gap Spacing
2 cm
6.25 cm
12.5cm
25 cm
cm
in.
NG*
Gf
NG
G
NG
G
NG
G
0.2
0.25
0.3
0.4
0.5
0.6
0.7
0.8
0.9
1.0
1.2
1.4
1.5
1.6
1.8
2.0
2.5
3.0
4.0
5.0
6.0
7.0
8.0
9.0
10.0
12.0
12.5
15
17.5
20
22.5
25
30
40
0.079
,098
.118
.158
.197
.236
.276
.315
.354
.394
.472
.551
.591
.630
.709
.787
.984
1.181
1.575
1,969
2.362
2.756
3.15
3.543
3.937
4.724
4.921
5.906
6.89
7.874
8.858
9.843
11.811
15.748
5.6
5.6
6.5
6.5
8.0
10.3
12.5
14.8
17.0
18.9
20.8
22.6
25.9
28.9
8.0
10.3
12.5
14.6
16.7
18,6
20.2
21.7
24.4
26.4
12.0
12.0
12.0
12.0
11
11
22.5
22.5
22.0
22.0
22
22
31.5
31.5
31.5
31.5
32
32
28.2
30 0
41.0
41.0
41.0
41.0
42
52
61
78
96
112
42
52
61
78
94
110
57.5
70.5
81.0
89.0
96.0
102,0
107.0
110.0
56.0
66.0
73.0
79.0
83.0
88.0
90.5
93.0
59.0
76.0
91.0
105,0
118.0
130.0
141.0
151.0
167.0
59.0
75.0
89,0
102.0
112.0
120.0
128.0
135.0
147.0
171
166
203
230
255
278
297
314
339
385
196
220
238
254
268
280
300
325
188.0
201,0
213.0
160.0
168.0
174.0
Values from F. W. Peek, Dielectric Phenomena in High Voltage Engineering, 3d ed., McGraw-Hill
Book Co. (1929).
* NG = electrodes balanced to ground,
t G •= one electrode grounded.
2-56
PROPEKTIES OF MATERIALS
Table 9 shows the influence of altitude on sparkover voltage at constant temperature
for uniform fields in gaps of various lengths. The table also is approximately correct for
closely spaced sphere gaps. Correction for the lower air temperatures shown is seldom
warranted unless the actual temperature of the air in the gap is known.
Table 9. Sparkover Voltages at High Altitudes
Ratio of sparkover voltage to sea-level sparkover in uniform fields
Sparkover Voltage at Constant
Altitude,
Standard
Pressure
Temperature
Unit =
1000 ft
Air Temp,
0°C
Relative
Pressure
Gap Spacing, cm
mm Hg
in. Hg
0.01
0.1
1.0
10.0
0
+ 15.0
760.0
29.92
1.000
1.000
1.000
1.000
1.000
5
+5.1
632.2
24.89
0.832
0.910
0.862
0.85
0.845
10
-4.8
522.6
20.58
0.687
0.828
0.742
0.719
0.712
15
-14.7
428.8
16.88
0.565
0.759
0.637
0.603
0.593
20
-24.6
349.1
13.75
0.459
0.695
0.545
0.505
0.493
25
-34.5
281.9
11.10
0.371
0.640
0.468
0.418
0.390
30
-44.4
225.6
8.88
0.296
0.592
0.399
0.345
0.331
35
-54.3
178.7
7.04
0.247
0.552
0.340
0.283
0.268
40
-55.0
140.7
5.54
0.185
0.517
0.291
0.232
0.217
45
-55.0
110.8
4.36
0.146
0.488
0.251
0.190
0. 175
50
-55.0
87.3
3.44
0.115
0.465
0.219
0.159
0. 141
The dielectric strength of gases is subject to large changes with impurities. At low
pressures, 0.1 per cent of argon in neon gas reduces the dielectric strength by 75 per cent.
Mercury vapor likewise lowers the sparkover voltage. At atmospheric pressure, the
addition of small amounts of carbon tetrachloride or chloroform vapor increases the di-
electric strength by 50 per cent. Table 10 shows the approximate relative dielectric
strength of gases. Although Freon (dichlorodifluoromethane) has a higher relative dielec-
tric strength, its vapor pressure varies from 9.3 psi at —40 deg cent to 139 at +40 deg
cent, whereas the pressure with sealed-in nitrogen increases by only 35 per cent in this
interval. Furthermore, if the Freon does break down, its decomposition products are
corrosive and carbon is deposited. Dry, oil-pumped nitrogen is undoubtedly the best
gas dielectric unless cooling is involved, which may necessitate the use of hydrogen.
Table 10. Approximate Relative Dielectric Strength of Gases
Gas
Pressure in Absolute Atmospheres
V3
1
2
4
8
Nitrogen
1 0
1 0
1 0
1 0
1 0
Air
0 9
0 9
0 9
0 9
I 0
Oxygen
0.9
0 8
0 g
0 8
Carbon dioxide
0 9
0 9
0 9
0 9
0 8
Hydrogen ,
0 6
0 6
0 6
0 6
Freon
2 4
2 2
2 2
2 2
Nitrogen plus carbon tetrachloride vapor
1 6
1 5
1 3
1 2
Helium
0.3
At frequencies above 10 kc the dielectric strength of air decreases slightly. Owing to
the low velocity of positive ions, they are not swept to the electrodes during one half cycle,
so that they remain to distort the field on the next half cycle. At frequencies above 60 kc,
a reduction of 7 to 13 per cent in breakdown voltage is to be expected, but no further de-
crease occurs up to at least several megacycles. If the gap is illuminated with ultraviolet
light, a decrease of 17 to 20 per cent is obtained.
MAGNETIC MATERIALS
By R. M.TBozorth and R. A. Chegwidden
Of all the common elements only iron, cobalt, and nickel have magnetic properties
greatly different from those of air or vacuum. The magnetic materials in common use
consequently contain at least one of these elements and sometimes all three These
MAGNETIC CHAEACTEEISTICS
2-57
materials, called ferromagnetic, make possible the operation of motors, generators, trans-
formers, and practically all electromagnetic devices.
Non-ferromagnetic materials are of little importance on account of their magnetic
properties. They fall into two classes: paramagnetic materials which are but slightly
more magnetic than a vacuum, and are therefore attracted weakly by the poles of an
electromagnet, and diamagnetic materials which are repelled weakly by an electromagnet
Because the magnetic materials used in communication are almost without exception
ferromagnetic materials, this article will be devoted to a description of this class. They
may be divided into "high permeability" (or magnetically "soft") and "permanent
magnet" (or magnetically "hard") materials. Ferromagnetic materials are commonly
referred to as simply "magnetic" materials.
The magnetic properties of materials depend primarily on the nature of the atoms which
compose them. In magnetic materials the atoms are small permanent magnets that owe
their magnetic moments to uncompensated spinning electrons lying in electron shells
inside the atom. For a material to be ferromagnetic these shells must be incomplete (i.e.,
have spaces for more electrons than are present) and have an excess of electrons spinning
in one direction, and the atoms must be arranged in regular fashion on a space lattice,
with atom centers not too close together. The important elements whose atoms fulfil
these conditions occur in one part of the periodic table — they are iron, cobalt, and nickel.
Gadolinium has been found to be ferromagnetic, and manganese and chromium can also
give rise to ferromagnetism when alloyed or chemically combined with the right non-
ferromagnetic elements. The Heusler alloys are composed of manganese, aluminum, and
copper; in comparison with many of the alloys of iron, cobalt, and nickel, they are quite
inferior from a practical magnetic standpoint and have had no commercial use.
Magnetic properties depend also on crystal structure, state of strain, temperature, and
other factors.
8. MAGNETIC CHARACTERISTICS
MAGNETIZATION AND PERMEABILITY CURVES. The properties of magnetic
materials are usually described first of all by a magnetization curve such as that shown in
Fig. 1. Here the magnetic induction, B, in a ring sample is plotted against the magnetizing
.**!03
o
i-J
Z
He
IRON
-3-2-1 0 1 2 345
MAGNETIZING FORCE, H, IN OERSTEDS
PERMEABILITY, fd.
:> — w c»> ^ m o> -j o>
clO3 .
A
•"^^
4% Si IRON
|\
1 \
i i
f
/
s
\
\
/
\
U.6
\
\
/
\
\
\
\
/
\
Ll,H
\
/
'"--
•*^
\
V
1
V
"0 2 4 6 8 10 12
INDUCTION, B, IN KILOGAUSSES, OR
MAGNETIZING FORCE,H,IN OERSTEDS
FIG. 1.
Magnetization Curve and Hysteresis
Loop for Annealed Iron Ring
FIG. 2.
Typical Permeability Curves for Hot-
rolled 4 Per Cent Silicon Iron
force, H. B is a measure of the amount of the magnetization; it is denned specifically
below under "Definitions." H represents the magnetizing force required to produce the
magnetic induction, B; it is usually measured hi oersteds or in ampere-turns per inch. The
magnetic induction is sometimes described in terms of the intensity of magnetization, I,
equal to (B — H)/&ir. The increase in induction due to the material alone is B — H,
sometimes called the intrinsic induction; this quantity becomes important when the mag-
netizing force is high, e.g., when determining Bs, the saturation induction, highest attain-
able value of B — H in a material.
The ease with which a magnetic material can be magnetized is measured by the ratio
B/H, called the permeability, \i. Typical permeability curves plotted against B and H
are shown for a sample of 4 per cent silicon-iron in Fig. 2.
2-58
PROPERTIES OF MATERIALS
In communication work, the permeability in low fields is especially important. Figure 3
shows the characteristic ju, H curves for several common materials ; in the lowest fields the
curves usually become straight lines.
«XIO3
35
3O
3.
<•
I'-
10
5
/
/
^
X0.014-IN. 4-79MO
PERMALLOY
^-
^
•==.
0.001- IN. 4 -1
PERMALLOY
1 45 |
PERMALLOY
9 MO
°c
> O.Ol O.O2 0,03 O.C
MAGNETI
FIG. 3. Characteristic ft vs H Ci
1
4.0
3.5
3.0
2.5
2.0
1.5
1.0
as
<103
1
/
1 PERMALLOY
/
'
/
/
3 PER CENT
SILICON -IRON/
^x
X
^
|X
/
IRON
NICKEL
=-
—•— —
^eu
— d?
^-— —
—
ni
—
O O.1 0.2
FORCE , H
0s JT Curves at Low Magnetizing Forces
Hysteresis Loops. Other important properties of magnetic materials are shown by
the hysteresis loop produced when B is plotted against H, as H is increased to a maximum,
decreased to zero, increased to a maximum in the negative direction, again reduced to zero^
and finally increased to the first Tn.fl.yJTmi.Tn as shown by the dotted line in Fig. 1. The
values of B and of H at which this curve crosses the axes are called respectively the residual
induction, Br, and coercive force, Hc, as indicated in the figure. The area enclosed within
the hysteresis loop is a measure of the magnetic energy transferred into heat during the
cycle and is designated Wh> Quantitatively
in ergs per cm3 when B and H are in
8
oersteds, respectively.
0.12 0.16 0.20
Fia. 4.
-0.12 -0.08 -0.04 0 0.04 '0.08
MAGNETIZING FORCE, H
Minor Hysteresis Loops Shown at Various Points on the Major Loop for a Specimen of 4-79
-Molybdenum Permalloy
MAGNETIC CHARACTERISTICS
2-59
Demagnetization Curve. That part of the hysteresis loop that lies in the second
quadrant, extending from Br to Hc in Fig. 1, is called the demagnetization curve and is
especially important for the description of permanent-magnet materials. This is de-
scribed more fully in Article 10 and Fig. 10. Hysteresis loops which do not have equal
excursions of H (and B} in opposite directions are unsymmetric or minor loops. Some of
these are shown in Fig. 4. In a minor loop the ratio of the total change in B, AS, to the
total change in H, AH, is called the incremental permeability MA = AB/AH. In the limit
as AB and AH approach 0, the incremental permeability is the reversible permeability, /^-.
This is sometimes referred to as superposed permeability, and is discussed in more detail
in Article 15 (Fig. 24).
Air Gaps. When an air gap is cut in a closed magnetic circuit, such as a ring sample,
magnetic poles are produced on either side of the break, and the apparent permeability of
the material is reduced because of the reluctance of the gap. The effect of even a small air
gap in a high-permeability circuit may be very appreciable. See Fig. 5, and Fig. 19 of
Article 15.
xio3
0 2 4 6 8 10 12 14 16 18 20 22 24 26 28 30 32
APPLIED MAGNETIZING FORCE, H
FIG. 5. Magnetization Curves and Parts of Hysteresis Loops Showing Effect of 0.005-in. Air Gap Cut
in a Silicon Iron Ring 2-in. I.D. by 3-in. O.D.
Eddy-current Loss. When magnetic fields are varied with some rapidity, as they are
in most machinery, the material is subject not only to the hysteresis loss already described
but also to eddy-current loss. This results from the flow of electric currents within the
material, induced by the changing flux in them. They increase with increase in the fre-
quency, conductivity, and permeability of the material. Since time is required for these
currents to build up and to decay, the application of a varying field is accompanied by a
delay in the corresponding magnetic induction. The summation of the hysteresis and
eddy-current losses is frequently called the core loss or iron loss of the material.
DEFINITIONS. The following definitions are taken from ASTM Specification A127
which may be referred to for definitions of other terms relating to magnetic materials.
This list is in alphabetical order, for reference only.
Coercive Force. Hc. The magnetizing force required to bring the induction to zero in a magnetic
material which is in a symmetrically cyclically magnetized condition. The coercivtty is that property
of a material measured by the maximum value of the coercive force.
Induction, Intrinsic. B^. The excess of the induction in a magnetic material over the induction
in vacuum, for a given value of the magnetizing force. The equation for intrinsic induction is
Bt = B — H
Induction, Magnetic (Magnetic Flux Density). 2?. Flux per unit area through an element of area
at right angles to the direction of the flux. The cgs unit of induction is called the gauss (plural gausses)
and is defined by the equation:
Under a-c conditions 2?ma
dA
: may be calculated as follows :
B X 108
where E is in rms volts ; ff is the form factor.
2-60 PROPERTIES OF MATEKIALS
Induction, Normal. 5. The limiting induction, either positive or negative, in a magnetic material
which is in a symmetrically cyclically magnetized condition.
Induction, Residual. Br. The magnetic induction corresponding to zero magnetizing torce in a
magnetic material which is in a symmetrically cyclically magnetized condition. The retentimty is the
property of a magnetic material measured by the maximum value of the residual induction.
Induction, Saturation. B8. The maximum intrinsic induction possible m a material.
Magnetic Flux. c|>. A condition in a medium produced by a magnetomotive force, such that when
altered in magnitude a voltage is induced in an electric circuit^ linked with the flux. The cgs unit of
magnetic flux is called the maxwell and is denned by the equation:
e= _tf^X10-8
at
where e = induced emf in volts, and d^/dt = time rate of change of flux in maxwells per second.
Magnetizing Force. H. Magnetomotive force per unit length. The cgs unit is called the oersted
and is defined by the equation:
*-$
where F is in gilberts and I in centimeters. For a toroid, or at the center of a long solenoid, the mag-
netizing force in oersteds may be calculated as follows:
—
where J is in amperes and I is in centimeters.
Magnetomotive Force. jF. That which tends to produce a magnetic field. In magnetic testing
it is most commonly produced by a current flowing through a coil of wire, and its^ magnitude is propor-
tional to the current and to the number of turns. The cgs unit of magnetomotive force is called the
gilbert and is defined by the equation:
F = QArNI
where J is in amperes. Magnetomotive force may also result from a magnetized body.
Permeability, a-c. |iac- A-c permeability is variously defined, and the values obtained for a given
material depend on the methods and conditions of measurement. As measured by the Standard
Methods of Test for Magnetic Properties of Iron and Steel (ASTM Designation A34) , it is the ratio
of the maximum value of induction to the maximum value of the magnetizing force for a material in a
symmetrically cyclically magnetized condition.
It is sometimes defined as the ratio of the rms flux density to the rms magnetizing force. Some of
the factors which affect a-e permeability are thickness of laminations, frequency, and resistivity.
Permeability, Incremental. HA- The ratio of the cyclic change in magnetic induction to the cor-
responding cyclic change in magnetizing force when the mean induction differs from zero.
Permeability, Initial, \LQ. The slope of the normal induction curve at zero magnetizing force.
•Permeability, Normal. (A. The ratio of the normal induction to the corresponding magnetizing
force. In the cgs system the flux density in a vacuum is numerically equal to the magnetizing force,
and, consequently, the magnetic permeability is numerically equal to the ratio of the flux density to
the magnetizing force. Thus:
B
» = H
Note: In a non-isotropic medium the permeability is a function of the orientation of the medium,
since, in general, the magnetizing force and the magnetic flux are not parallel.
Permeability, Reversible. HT. The incremental permeability when the cyclic change in induction
is vanishingly small,.
9. HIGH-PERMEABILITY MATERIALS
Preparation and Heat Treatment. In many applications such as motors, generators,
transformers and relays, it is desirable to have materials of high permeability. The com-
mon materials used are iron, silicon-iron alloys, and iron-nickel alloys to which various
other metals have been added. Commercial materials are usually melted in open-hearth
or electric furnaces, poured to form ingots, then rolled to slabs and finally to sheets or
rods of the required imensions. After fabrication into the final form in which they are to
be used, they must be subjected to a heat treatment which is appropriate to the particular
alloy, in order to develop their best magnetic qualities. These heat treatments usually
consist of heating to some temperature lying between 800 and 1200 deg cent and cooling
at a definite rate to room temperature. Figure 6 shows magnetization curves for ingot
iron, (1) as hot and cold rolled to final size, (2) as annealed at 900 deg cent for 1 hour, and
(3) after heat treatment at the unusually high temperature of 1400 deg cent for 6 hours.
The anneal at 900 deg cent may be referred to as a strain-relief anneal; that at the higher
temperature as a purifying anneal because during the process some of the impurities have
been removed from the iron.
^ In processes involving annealing, account must be taken of phase transformations and
"order-disorder" phenomena (orderly arrangements of the atoms) like those found in iron
HIGH-PERMEABILITY MATERIALS
2-61
and Permalloy, respectively. In some materials, such as the nickel-manganese alloys, a
magnetic material may be made non-magnetic by cooling rapidly from a high temperature
and thus preserving the disorderly distribution of nickel and manganese atoms stable at
this temperature. In the iron-nickel alloys containing 50 to 80 per cent nickel, marked
changes in properties are
produced by annealing
in the presence of a mag-
netic field.
Magnetic Elements.
Of the magnetic ele-
ments, iron, cobalt, and
nickel, iron is the only
one used commercially
to any considerable ex-
tent in unalloyed form.
It is made in large ton-
nages for motors, gen-
erators, and relays. Its
characteristic properties
are described in Fig. 9
and Table 1. Nickel
finds a limited use be-
cause of its magneto-
strictive properties, for
example in supersonic FIG. 6. Effect of Heat Treatment on the Magnetic Properties of Iron
underwater apparatus.
Iron-silicon Alloys. Next to unalloyed iron, these alloys are used in the greatest
quantities, in power transformers, motors, generators, relays, and receivers. The addition
of silicon increases the resistivity and so cuts down the power loss due to eddy currents,
and it also has some effect in increasing the permeability and decreasing the hysteresis
loss. Various commercial grades are available containing up to about 5 per cent silicon.
Great advances have been made in the last few years by fabricating the sheet by cold roll-
ing instead of hot rolling. As with most magnetic materials, the iron-silicon crystals are
most easily magnetized along one particular crystallographic direction, and the cold roll-
ing and associated heat-treating processes are adjusted to orient the crystals so that as
many as possible have their directions of easy magnetization aligned in the direction of
rolling. Material made in this manner is called grain oriented. The grain-orienting process
5 6 7 8 9 10
MAGNETIZING FORCE, H
32
28
24
±
.20
-
j
xio3
^
""""^
^
X
GRAIN ORIENTED
3% SI IRON
HOT ROLLED
3.6% Si. IRON
/
'
\
/
\
v
/
\
\
o 10
u
1,2
ill
CL
6
4
0
0
A
/
ALONG
GRAIN
\
/
i-
-~-
— --.
**««fc.
\
^
?Z*~
*""
\
**
---.
""^
•v^
\
\
s
•**^
^^•««*,
•i^v
*5Sa
N
jk
X
1 2 34 5 6 7 8 9 10 11 12 13 14 15 16 17X103
INDUCTION ,B
FIG. 7. Comparison of the M «s B Curves for Samples of Hot-rolled and Grain-oriented Silicon Iron
increases the permeability and reduces hysteresis loss. The increase in permeability, how-
ever, is effective only when the sheet is magnetized in the direction in which it is rolled,
and in most other directions the permeability is lowered. Grain-oriented silicon-iron is
available in grades containing up to slightly over 3 per cent silicon. Properties of the
grain-oriented material containing 3 per cent silicon are compared with the hot-rolled
product in Fig. 7.
2-62 PROPERTIES OF MATERIALS
i
Iron-nickel Alloys. These alloys are used when particularly high quality is desired,
usually in transformers of various kinds and in magnetic shields. Their permeabilities
are much greater than those of other alloys, and they have high resistivity and low energy
loss. The most important binary alloys contain 78 per cent nickel and 45 to 50 per cent
nickel. The former, called 78 Permalloy or Permalloy A, has a high initial permeability
(about 10,000) and a low coercivity (0.05) and requires special heat treatment for the
development of these properties. After the usual anneal at 1000 to 1100 deg cent it must
be cooled rapidly in order to develop maximum quality. The iron-nickel alloys containing
45 to 50 per cent nickel are useful in certain relays, transformers, receivers, and other
apparatus. They have reasonably high permeabilities and incremental permeabilities,
and their saturation inductions and resistivities are higher than those of the 78 per cent
alloy. The cooling rate from the annealing temperature is not critical for these alloys.
Another development in this field is the grain-oriented 50 per cent nickel-iron alloy,
originated in Germany and called Permenorm 5000-Z. After special heat treatment, this
material exhibits hysteresis loops which are practically rectangular. The grain orienta-
tion is accomplished by a 99 per cent cold reduction before the final heat treatment.
When higher resistivities are required, other elements are added to the iron-nickel alloys,
and it is often found that the resulting alloy has also higher initial and maximum perme-
abilities. One of the most useful of these is Molybdenum Permalloy containing 4 per cent
molybdenum and 79 per cent nickel. Similar properties are obtained in Mumetal con-
taining 2 per cent chromium, 5 per cent copper, and 75 per cent nickel. Initial perme-
abilities of 20,000 to 30,000 and maximum permeabilities of about 100,000 are often found
in these alloys. The molybdenum Permalloy must be heat-treated under non-oxidizing
conditions and preferably cooled at a definite rate; the Mumetal must be heat-treated in a
hydrogen atmosphere for best results. An alloy containing 5 per cent molybdenum and
79 per cent nickel is called Supermalloy and has an initial permeability of 50,000 to 150,000
and a maximum permeability of about 1,000,000. These properties are obtained by con-
trolled melting of suitable raw materials, heat treating in hydrogen at 1300 deg cent, and
cooling at a critical rate.
Some interesting properties have been obtained in alloys containing nickel, iron, and
cobalt, called Perminvars. A typical alloy contains 45 per cent nickel, 25 per cent cobalt,
and 30 per cent iron, and its permeability is characteristically independent of magnetizing
force over a relatively large range. To retain this property, however, it must never be
magnetized above this range. Above the range of constant permeability the hysteresis
loops have peculiar constricted forms with very low residual induction at intermediate
field strengths. At present these alloys are not being used commercially.
Iron-cobalt Alloys. Alloys of iron with approximately 35 per cent to 55 per cent
cobalt are remarkable in that the saturation, B8, is higher than that of either iron or co-
balt. One of these alloys, containing equal parts of iron and cobalt, is called Permendur;
it is useful where high flux densities are necessary as in the pole tips of electromagnets.
The binary alloys of iron and cobalt can be hot rolled and machined, but they are very
difficult to cold roll. Vanadium Permendur contains 2 per cent vanadium and equal parts
of iron and cobalt; the addition of vanadium makes it possible to cold-roll the alloy to thin
sheets. In this form it has found an important application in telephone diaphragms.
Vanadium Permendur can be machined and even punched after cold rolling, but it be-
comes somewhat brittle when annealed. At high inductions the superposed permeability
of the iron-cobalt alloys is higher than that of any other material (see Fig. 24) .
Other Alloys. Among the other alloys that have high permeability may be mentioned
aluminum-iron, molybdenum-iron, and Sendust, the last developed by the Japanese.
Aluminum-iron containing up to about 6 per cent aluminum has been produced having
magnetic properties somewhat better than the iron-silicon alloys, but because of manu-
facturing difficulties it has never been popular. In Japan high permeabilities have been
obtained in the alloy containing 14 to 15 per cent aluminum, called Alfer. Iron-molyb-
denum alloys also have good magnetic permeabilities at low and moderate flux densities
and are more ductile than the iron-silicon alloys. Although they are not in common use,
at teast one manufacturer is planning to market them. Sendust contains about 9 per cent
silicon, 5 per cent aluminum, and the rest iron. Both initial and maximum permeability
are high, the initial sometimes as high as 35,000. Sendust is an unusual high-permeability
material in that it is quite brittle and must be cast and ground to finished size. Because
of its brittleness, Sendust has been formed into powder and used, especially in Japan, in
pressed powder cores for loading coils and other coils for high-frequency circuits
Other materials are useful in powdered form for applications of this kind. Most impor-
tant among them are powdered Permalloy and Carbonyl iron. The former has the nominal
composition of 2 per cent molybdenum, 80 per cent nickel, and 18 per cent iron; it is
melted without the addition of a deoxidizer or desulfurizer, and after hot rolling it can
HIGH-PERMEABILITY MATERIALS
2-63
2-64
PROPERTIES OF MATERIALS
be crushed to a fine powder. It is then mixed with a small amount of insulation and pressed
into a solid core and heat-treated. The permeability varies, depending upon the amount
of insulation, from about 10 to 125. Both
hysteresis and eddy-current losses are ex-
tremely small, and the permeability is con-
stant over a large range of magnetizing force.
Carbonyl iron powder, prepared by de-
composing iron carbonyl, Fe(CO)5, in the
vapor phase, consists of small spheroids
which are later insulated and pressed. All
these powdered materials are used in the
cores of coils operating at high frequency;
Fig. 8 shows some of their properties.
Often, when the frequency is greater than
1 megacycle, a powder is used composed of
one of the iron oxides Fe2Os or FegO^ Also,
properly treated mixtures of complex f errites,
e.g., manganese and zinc ferrites, have been
found to have very high electrical resistivities
and initial permeabilities of the order of 1000.
Materials of this type, developed in Holland
under the name Ferroxcube, have been used
advantageously for certain types of high-
PERMEABILITY, JUL
^o8&888§§
"\
/
V ^
\
y
^x
X
— *
"
MOLYBDENUM
PERMALLOY
POWDER
CARBONYL IRON
TYPE 55
^
**
0 20 40 100 200 1000 2OOO 10.OC
INDUCTIONS
FIG. 8. Examples of Permeability Curves for
Cores of Molybdenum Permalloy and Iron Car-
bonyl Powders
frequency coils. The ferrites in general have much higher initial permeabilities but less
stability with temperature as compared with the insulated powder materials.
Many of the properties of the most important commercial magnetic materials of high
permeability are collected in Table 1 and Fig. 9.
PERMEABILITY, JJL
o.oot 0002 coo*, aoi 002 ao4 o.i 02 04 o.e 1.0
FIG. 9. Magnetization and Permeability Curves for Magnetic Materials in Common Use
Non-magnetic Materials. It is often desirable in dealing with magnetic circuits to
have a steel for structural purposes which is non-magnetic. One commonly used material
of this sort, called Lomu, contains about 10 per cent manganese, 8 per cent nickel and
the remainder iron; chromium and silicon are also sometimes added. Another material
is of the stainless-steel type containing 20 to 25 per cent nickel and 25 per cent chromium.
PERMANENT-MAGNET MATERIALS
2-65
10. PERMANENT-MAGNET MATERIALS
Permanent magnets are useful for their ability to maintain a magnetic field in space
without the aid of an external source of power. Since there is no heating, and since modern
alloys can produce very high fields, they are used extensively in loudspeakers, small gen-
erators, etc. The properties of these materials are best described by means of the de-
magnetization curve already mentioned. Typical curves for many of the common mate-
rials are shown in Fig. 10. In evaluating materials it is also desirable to use an energy
12
11
10
9
T>8
CD
%•>
I6
5
4
3
2
1
n
, —
^- —
/
^
/
f
w<
/
/ii
;
R6M,
K
I
Hi
1
ALNICO 5 I
/
i i
f
i
y
,
/r
1
/
*/
' 1
i
i
s
I
p
j
Cr
/
,
—
OXIDE !
— rT
T
4-
'*
-.-"*"'
7
/
ll
i
1
8OO 600 400
DEMAGNETIZING FORCE,
t 2 3
ENERGY PRODUCT,
4X106
FIG. 10. Demagnetization and Energy Product Curves of Some Important Permanent-magnet Mate-
rials, The materials corresponding to the abbreviations may be recognized by reference to Table 2.
product curve formed by plotting the product of B and H, BH, against the magnetic
induction B, for points on the demagnetization curve; this is plotted also in Fig. 10. Such
a curve is a measure of the energy that can be stored in the magnet, and the best single
criterion for the value of a permanent-magnet material is the maximum value of this
product, designated (BH)m- In the design of magnetic circuits involving permanent
magnets an attempt is usually made to have the magnetic induction in the magnet equal
to the B for which (BET) is equal to (BH}m.
The magnetic behavior of a magnet may be described by reference to Fig. 11. The
line OA depends on the dimensions of the magnet and is called the load line; it is fixed by
the demagnetizing action of the air gap in the magnetic circuit. When the external field
has been removed, B and H will be determined by some point on this line, preferably the
point for which (BH) is a maximum. It is common practice to "stabilize1* a magnet by
applying a small negative magnetizing field (point C) and then removing it (point D).
Extraneous disturbing fields will then cause changes in induction corresponding to minor
loops such as CDEC. The minor loops in the third quadrant, under the demagnetizing
curve, have slopes approximately the same as the slope of the demagnetizing curve just
below the point B; they are important in predicting the changes in induction that occur,
e.g., in generators.
Permanent-magnet materials may be classified under the following headings:
Carbon steel with or without alloying elements.
Dispersion-hardened alloys.
Types heat-treated in a magnetic field.
Ductile alloys.
Powdered materials.
Miscellaneous special materials
2-66
PROPERTIES OF MATERIALS
4
Hd
FIG. 11. Curves Useful in the Design of Permanent Magnets. See text.
60O 4OO 2OO
DEMAGNETIZING FORCE, H
23
ENERGY PRODUCT,
5XI06
Carbon Steels. The carbon steels are so called because they depend upon carbon
compounds for their permanent-magnet qualities. These materials are usually prepared
by hot rolling to finished size and quenching from about 800 to 950 deg cent in water or oil.
Their permanent-magnet characteristics tend to deteriorate with time, and it is customary
to pre-age such magnets before use by maintaining them for many hours at temperatures
between 100 and 150 deg cent. Although their magnetic properties are not of very high
quality, many of the carbon-steel magnet alloys are very useful because of their low cost.
The most common steels are carbon-manganese, chromium, tungsten, and cobalt steels*
There is a great variety of materials of this kind containing various percentages of the
alloying elements and about 0.8 per -cent carbon. Representative alloys have been in-
cluded in Table 2. The coercive force and energy product, as well as the cost, usually
increase with the alloying element. The highest energy product obtained in this group is
about 1.0 X 106.
Dispersion-hardening Allays. These alloys contain no essential carbon but depend
for their hardening upon the precipitation of one solid phase in another. They are ordi-
narily heated to 1300 deg cent and quenched in air or oil and are subsequently maintained
at 600 to 700 deg cent for several hours; they are therefore often referred to as "age-
hardening" alloys. Generally they are quite brittle and, with the exception of one type,,
must be cast and ground to final size. One of the first alloys of this type to be used com-
mercially contains 71 per cent iron, 12 per cent cobalt, and 17 per cent molybdenum; it
is called Remdttoy or Comol. This alloy may be hot-rolled and machined to required size
like the carbon steels. To give it permanent-magnet qualities, it is quenched from 1200
deg cent and aged at 700 deg cent for about an hour. Like most cuspersion-hardening
alloys, the properties of Remalloy do not change appreciably with time. It has found
use in meters, receivers, and other devices.
Large quantities of dispersion-hardening alloys are made of the iron-nickel-aluminum
type to which have been added cobalt, copper, or titanium. All these alloys, called in
this country the Alnicos, are brittle and must be cast and ground to size. The addition of
titanium up to S per cent is sometimes effective in causing high coercive force. Heat
treatments and properties are given in Table 2.
Types Heat-treated in a Magnetic Field. The most important of the dispersion-
hardening alloys was developed in Holland as TiconaL and, with slight variations, is
known in the United States as Alnico 5 and in England as Alcomax. The alloy of the
proper composition as given in the table is heated to 1300 deg cent and then cooled in air
in the presence of a strong magnetic field which must be applied to the magnet in the
direction in which the best properties are desired. After aging at about 600 deg cent
energy products as high as 5 X 106 are obtained.
PERMANENT-MAGNET MATERIALS
2-67
£•§ a
~a.g
oo oo «o oo co oo "<r 01
5 OO O
4 rf\ r^
§1
o g,
Pq a
OQ
trj fl
t-H 0)
d
.2
II
^
1?
a^
<!
W W t
m t>i
> o o •
ooooooooooooooooooovno
ooooooooooooooooooot^o
t>.ooir\«J^w^r^rM^ir\u-\t-^^rc^'«r'^fMoeMvOLn«r\
vn vo \o LO -«• <•
ooo
\ ; ; ; ; o o o
:pq pq pq
00 00 00
O'O' O*
o 5? '
0*^
*• •
:oo
O«-
0
^S*
^1^
1— «<\ -O •—
•v^«»7
» ««0'C
50 I
I : :
: riR : :
. | o* .
' E •« ^ :
-S g §r^'
Ill2
-I
^ ^* I ^
Ula^-
iall-s's
^sll^g
11 n ii ii ii
cq
J3
.9
o
J-l
N-
S «P
2-68
PROPERTIES OF MATERIALS
The interesting oxide magnets made by the Japanese also require a strong magnetic
field for developing their best properties. The proper amounts of iron and cobalt oxides
(Fe203 Fe304, and Co203) are pressed and heated to 1000 deg cent. They are then
cooled and crushed and pressed to final form, then reheated to 1000 deg cent, and finally
cooled in a strong magnetic field. Large variations are found in coercivity and retentiyity,
depending on how the oxides are mixed and treated; Hc ranges from 600 to 1000 and #r
from 4000 to 1500. This material is unusually light in weight and has exceptionally high
resistivity. One product, marketed under the trade name Vectohte, has a coercivity of
900 and a retentivity of 1600.
Ductile Alloys. Within the last few years a number of ductile permanent-magnet
alloys have appeared on the market. The largest application has been m wire and tape
form for the magnetic recording of speech. The first alloys of this type were based on the
German material containing 20 per cent iron, 20 per cent nickel, and 60 per cent copper,
known in this country as Cunife. Another variation, called Cunico, contains cobalt.
Most of these alloys can be cold-drawn to fine wires; in fact, such cold reduction is often
necessary to develop their best properties. Viccdloy, made of iron, cobalt, and vanadium,
is another alloy of this type. Its properties also depend upon the amount of cold reduction,
and an energy product of 1.5 X 106 can be developed after cold rolling and annealing at
about 700 deg cent. By drastic cold reductions energy products as high as 4 X 10 can
be obtained.
Powdered Materials. Several of the brittle alloys mentioned above can be produced
from powders which are pressed into the desired shape, sintered at a high temperature,
and heat-treated to give the best magnetic properties. This is often advantageous in
producing small magnets, when the methods of powder metallurgy can be used. Alnico 2
is important in this class, and Alnico 5 has been used on an experimental scale.
A recent development is material obtained by pressing powder of very fine size, such
as that produced by the reduction of iron compounds at low temperature. One product,
manufactured in France, is composed essentially of fine particles of iron, sometimes with
admixture of cobalt, and has properties much like those of Alnico 2.
Special Alloys. A few other alloys are worthy of brief mention. These are the cobalt-
platinum alloys, the manganese-silver-aluminum alloy (Silmanal), and certain alloys
formed by electrodeposition on a mercury sur-
face, e.g., iron with a small admixture of zinc
or iron-cobalt-nickel-aluminum alloys. Ex-
perimentally this alloy has been made with
coercivities of 400 to 500 and retentivities of
9000 to 11,000.
£4
SATURATION, 85
rPLm
,/Mo
UPPER
PORTION
MIDDLE
PORTION
LOWER PORTION
11. MAGNETIZATION CURVE
In this section will be considered briefly the
nature of the changes in magnetization that
correspond to different parts of the magneti-
zation curve, and some relations valid in each
part.
The magnetization curve may be divided
into three parts separated by the "instep" and
"knee" (see Fig. 12). At the instep the curve
takes a sudden upward turn and the perme-
ability increases rapidly. At the knee this
trend is reversed and the curve becomes more
and more horizontal and approaches asympto-
tically to saturation. In each of the three
parts of the curve, magnetization proceeds by
a different mechanism, as described below.
A magnetic material is composed of many
small magnetized regions or domains, each of
which is always magnetized to saturation in
some one direction. When the material as a
whole is unmagnetized, these domains are ar-
ranged in various directions so that the net magnetization of the material is zero. The
effect of the field is to change either the direction in which the domains are magnetized or
to change the volume of some of the domains at the expense of their neighbors. This may
be made clear by reference to Fig. 13, where the domains are represented by arrows indi-
O 0.1 0.2 0.3 0.4 0^
MAGNETIZING FORCE, H
FIG.! 12. Magnetization Curve Showing
the Points of Special Interest, and Division
into Three Main Parts
EFFECT OF TEMPERATURE
2-69
eating the directions in which they are magnetized. The directions of stable magn^etiza-
tion are determined in an annealed material by the magnetic properties of the crystals of
which it is composed, and in severely cold- worked material by the internal strains present.
In the first part of the magnetization curve, below the instep, magnetization proceeds
by small displacements of the boundaries between domains, a process illustrated in part
(6) of Fig. 13. In this portion the permeability usually increases linearly with magnetiz-
ing force:
M = a -j- bH
In the second part of the curve, between the instep and the knee, the domains change
direction suddenly and the magnetization changes
from one direction of stable magnetization to an-
other. In this section Steinmetz* law of hysteresis
is applicable:
Wh = T/S1-6
(b) PARTIAL MAGNETIZATION
(C) SUDDEN REVERSALS COMPLETE
(KNEE OF MAGNETIZATION CURVE)
* V
(d) SATURATED, DOMAINS ROTATED
IN HIGH FIELD
CRYSTAL
AXES
MAGNETIC
FIELD
200 400 600
TEMPERATUR£,eC
800
FIG. 13. Diagram Illustrating Changes
in Domain Structure with Magnetiza-
tion in a Single Crystal of Iron
FIG. 14. The Magnetic Induction of Iron Meas-
ured at Various Temperatures, with Various Im-
pressed Fields
In the third section the domains rotate smoothly from the stable directions indicated in
(c) into parallelism with the magnetic field as indicated in (d) ; here the Frohlich-Kennelly
relation
i - c + dH
M
is approximately valid.
Evidence for the domain structure of materials is found in the Barkhausen effect, which
proves that sudden changes in magnetization occur in the middle section of the magnetiza-
tion curve, and in the existence of powder patterns which can be seen under a microscope
and which show that the magnetic field at the surface of a demagnetized magnetic mate-
rial varies from place to place over regions about 0.1 mm apart.
12. EFFECT OF TEMPERATURE
The magnetization of a material can be altered not only by changing the magnetic field
but also by varying mechanical stress or temperature. Temperature affects the magnetic
properties of all materials, in a way that depends on the induction and the character of
the material. Figure 14 shows this effect for iron. Eventually, as the temperature is
raised, the material becomes non-magnetic, the temperature at which this occurs being
2-70
PROPERTIES OF MATERIALS
called the Curie point of the material. When a high constant magnetic field is present, the
magnetization decreases continually as the temperature increases, and at a faster and
faster rate as the Curie point is approached. When a low field is present, the permeability
first increases with temperature and then decreases again and approaches 1 at the Curie
For some applications it is desirable to have a material with a permeability that de-
creases rapidly as the temperature increases. These materials are used in compensating
permanent magnets for changing temperature and for stabilizing pressed powdered cores
to make their inductance independent of temperature. The alloys used for this purpose
have a Curie point near room temperature so that the material loses its magnetism rapidly
as the temperature increases in this region. One such alloy contains about 30 per cent
nickel and the rest iron; it has been used for compensating permanent magnets. Another
type, containing 80 per cent nickel, 12.5 per cent molybdenum, and the rest iron, is com-
monly used for stabilizing pressed powdered Permalloy cores. Still another type contains
about 35 per cent nickel, 5 per cent chromium, 0.3 per cent silicon, and the rest iron.
13. STRESS AND MAGNETOSTRICTION
Figure 15 shows the way in which the magnetization may be affected by the application
of tensile stress. A tension well within the elastic limit of the material will increase the
magnetization of 45 Permalloy and decrease that of pure nickel. Under certain conditions
the permeability of some materials is increased by a factor of 50 by a stress within the
elastic limit. Materials whose permeabilities are increased by tension are said to have
positive magnetostriction, because they expand a few parts per million when they are
TENSION =2800 LB/1N.2
r— i r
234
MAGNETIZING FORCE, H
-30
7
I
NICKEL
FIG. 15. Magnetization Curves for 45 Permalloy and
Nickel as Affected by Tension
40 80 120 160 200 24O 280
MAGNETIZING FORCE , H
FIG. 16. Fractional Change in Length with
Magnetizing Force for 45 Permalloy (Posi-
tive Magnetostriction) and for Nickel (Neg-
ative Magnetostriction)
magnetized; conversely, the permeability is decreased by tension if magnetization causes
contraction of the material (negative magnetostriction, as in nickel). Some materials,
like iron, have positive magnetostriction in low fields and negative magnetostriction in
high fields.
Figure 16 shows how 46 Permalloy and nickel change in length as the field strength
increases. Such magnetostriction is capable of converting magnetic energy into mechanical
energy, and nickel is often used in magnetostriction oscillators to produce supersonic
vibrations in air or under water, where they are effective in sound ranging. The Japanese
have used a new alloy, Alfer, containing 13 per cent aluminum and the rest iron, for mag-
netostriction oscillators; its magnetostriction is about the same in magnitude as that of
nickel, but is opposite in sign.
14. EFFECT OF FREQUENCY
_ When the field acting on a magnetic material is alternated rapidly, eddy currents are
induced in the material. They act so as to keep the a-c field from penetrating effectively
EFFECT OF FREQUENCY
2-71
more than a certain distance below the surface; this distance is measured in a rough way
by the expression: __
wherein jj, — true permeability (d-c) .
p = 103 times resistivity in microhm-centimeters.
/ = frequency in cycles per second.
The properties of the material are affected in three ways: (1) the effective permeability
is reduced, (2) the energy loss in the material is increased, and (3) there is a time lag
between the magnetizing force and the corresponding induction.
Only under certain restricted conditions can the effects of alternating current be pre-
dicted with any assurance of correctness. When the permeability is constant, as it usually
is only when B is very small, the effective permeability, £ (as determined with an induc-
tance bridge) is given by the relation :
sinh 6 + sin d
H 6 cosh 6 + cos d
in which 6 = Z-rrtVuf/p — t/s.
t — thickness of sheet in centimeters.
Effective permeabilities, calculated by means of this equation, are compared with actual
measurements in Fig. 17.
20'
18
16
(3.
>>
Zi
512
<
UJ
iio
s
ge
i'
u.
UJ
4
2
n
do2
1^-.
-„..
^~^<
^^
__
^*s«
— -«.
X
X;
x;
^
N
N
\
V
Y\
\ \
X
^
\
\
\
\
\
45 PERMALLOY
THEORETICAL
ACTUAL
\
"f\
\
^
\
•v^J
'4
k
""v.
Si .
**•*.
\
^sv
-^
^
"*s.
^•^,
-^^.
— «.
>~»
0,04 0.1 0.2 0.4 0.6 a8 I 2 34 6 8 10 20 30 40 60 80100
FREQUENCY IN KILOCYCLES PER SECOND
FIG. 17. Change in Effective Permeability with Frequency for 45 Permalloy of Different Thicknesses
When B ^> 1 (at high frequencies) this expression reduces to:
1 jos
Similar expressions are applicable to specimens in the form of wire or cylinders.
When /x is constant and 6 < 1 (frequency and induction low) the power loss may be
expressed by the equation:
- = 27r/(^o + hB + ef)
Ju
in which R = excess of a-c resistance (by a-c bridge) over d-c resistance, in ohms.
L = inductance of coil in henrys.
B = maximum induction in gausses.
This relation is especially adapted to materials used in communication circuits in which
there are feeble alternating currents. The constants h and e measure the hysteresis and
2-72
PROPERTIES OF MATERIALS
eddy-current losses, respectively, and ho is of unknown origin, important only at the low-
est B's.
At low frequencies (6 < 1) and high inductions (5 = 1000 to 14,000 in silicon-iron), the
power loss in ergs per centimeter3 per second is:
W = rjB^f + eB2/2
The hysteresis constant, 77, and the eddy-current constant, e, can be determined in an
approximate way by plotting W/f vs. / for given values of B. At high frequencies eddy-
current loss is usually more important than hysteresis loss, and is given in ergs per cen-
timeter3 per second by the relation:
in which J-? is the value of B averaged over the cross-section of the sheet.
At frequencies higher than 108 cps the true permeability, ju, of magnetic materials
begins to decrease substantially, approaching a value of the order of 1 at frequencies
around 109 to 1011 cps.
Magnetization also affects the resistivity of magnetic materials. The change is almost
invariably an increase in resistivity with magnetization, the amount of the increase vary-
ing from less than 1 per cent to about 5 or 10 per cent at room temperature, and even more
at low temperatures. Similarly Young's modulus may be changed by about 10 per cent
by magnetizing to saturation. Unusual variations are also observed in specific heat,
thermal expansion, and other physical properties of magnetic materials.
15. MEASUREMENT OF MAGNETIC CHARACTERISTICS
Although it requires many different measurements to determine all the magnetic char-
acteristics of a material, the most important properties can be obtained from a magnetiza-
tion curve and hysteresis loop, an a-c measurement of the permeability and losses, and a
measurement of the incremental permeability at various polarizing inductions.
Of the several methods that can be used for measuring magnetic properties, the ballistic
ring test, due to Rowland, is perhaps the most reliable. In this test, a ring sample is wound
with two uniformly distributed windings, consisting of a primary connected to a source of
current, and a secondary connected to a ballistic galvanometer or fluxmeter. The induction
produced by current in the primary winding is observed in terms of the fluxmeter deflec-
tion as the primary current is changed suddenly or reversed. The use of a ring sample
eliminates the possibility of errors due to air gaps. To obtain uniformity of magnetizing
force throughout the sample, the ratio of the outside diameter to the inside diameter of
the ring should be not greater than 1.2. Figure 18 shows a typical electrical circuit for
FIG. 18. Simplified Diagram of a "Ballistic Test" Circuit
fl n ^ including * m^tual Muctance for calibrating the galvanometer or
flurmeter, <?, and resistances R and switches S for regulating and changing the current in
the primary winding, P. The field is calculated using the relation-
MEASUREMENT OF MAGNETIC CHARACTERISTICS 2-73
and the induction using the expression :
3 - Kd
ICM X 108S
8CN3A,
in these equations Nf = number of turns in primary winding.
/ = primary current in amperes.
d — mean diameter of ring in centimeters.
Ic — calibrating current in amperes.
M = calibrating mutual inductance in henrys.
dc = calibrating deflection resulting from a reversal of I0.
Ns = number of turns in secondary winding.
A8 — sectional area of sample in square centimeters.
5 — fiuxmeter deflection resulting from reversal of current in primary
winding.
Straight bar or rod samples are sometimes tested with this circuit. A long solenoid is
used for producing the magnetizing force, and the secondary winding or search coil is
placed around a short central portion of the sample. However, under these circumstances
the true magnetizing force is difficult to determine because the field from the magnetic
poles produced at the ends of the sample reacts with the field of the solenoid. The field
created by the sample itself is sometimes called the end effect or demagnetizing field. Its
value is usually specified by the demagnetising factor, JV, which depends on the ratio
length/diameter of the rod. The field, H, acting at the center of the rod is the resultant
of the field in the solenoid, J?o, and the demagnetizing field:
H = Ho - jj- (B - H)
The apparent permeability, //, is given by B/HQ, and its relation to the true permeabil-
ity, ju is given by:
I = I _ ~
M ~~ /*' 4?r
The relation between p and JJL' for cylindrical rods is shown graphically in Fig. 19.
LENGTH
DIAMETER
_10 20 40 60 IO2
IO 20 40 60 To2
105
JO3 IO4
TRUE PERMEABILITY, /JL
FIG. 19. Relation of the Apparent Permeability to the True Permeability for Cylindrical Rods of
Various Ratios, m, of Length to Diameter. Also, Demagnetizing Factors, N/4ir, as Dependent on m.
2-74
PROPERTIES OF MATERIALS
Various types of permeameters are also used with the circuit shown in Fig. 18. They
are especially useful for measuring permanent-magnet materials. Permeameters usually
are designed to test straight bar samples clamped against a yoke of very low reluctance.
Measurement of samples of high permeability, so tested, are subject to error due princi-
pally to the effects of the air gaps in the circuit. Only a few of the many types will be
described.
The Fahy permeameter is commonly used for testing materials like iron and silicon-iron
as well as some of the magnet steels of relatively low coercive force. It is suitable for tests
at magnetizing forces up to 300 oersteds. This instrument, shown in Fig. 20, has one
large magnetizing winding on a yoke of silicon-iron. Pole pieces extending from either
end of the yoke are arranged so that bar samples can be clamped to them. The magnetiz-
ing force is measured by an air-core solenoid (H coil) mounted across the ends of the pole
pieces and above the sample. A winding enclosing the sample acts as a secondary (B coil)
and measures the induction with the aid of a galvanometer as in Fig. 18.
MAGNETIZING
• COIL
FIG. 20. Descriptive Drawing of the Fahy Perme-
ameter
SPECIMEN
FIG. 21. Descriptive Drawing of the Babbitt
Permeameter
The Babbitt permeameter (see Fig. 21) can be used for testing at magnetizing forces as
high as 1000 oersteds. Several different high-permeability materials are used in the yoke
to give low reluctance over a wide range of magnetizing force, and the magnetizing coil
encloses the sample instead of being wound on the yoke alone as in the Fahy. Smaller
windings are placed on the yoke to compensate for the reluctance of the air gaps. Mag-
netizing force and induction are measured with H and B coils placed near and around the
middle of the sample.
More accurate tests of high-permeability materials can be made by means of the Bur-
rows permeameter. This type requires two samples clamped between two connecting yokes
of high-permeability material completing the magnetic circuit. In addition to the mag-
netizing coils around the samples, there are compensating coils around each end of the
samples to give more adequate corrections for the effect of the air gaps at the joints. B
coils are wound around the middle of each sample, and two search coils are placed on
either side of each B coil. With proper adjustment the conditions of test more nearly
approach those in the ring test, but the test is time-consuming because of the number of
adjustments required.
Small air gaps are not very important when testing permanent-magnet alloys, but
modern magnet materials require permeameters that can produce very high magnetizing
fields. The saturation permeameter and the high-H permeameter are frequently used for
this purpose.
The saturation permeameter is very similar to the Babbitt permeameter except that the
magnetizing coil is larger and artificially cooled, and no compensating coils are used on
the yoke. Magnetizing forces as high as 2500 oersteds are readily obtained with this
instrument.
The higbrH-permeameter developed by the Bureau of Standards can produce even more
powerful fields and can be used to test any of the modern permanent-magnet alloys. In
this permeameter four large coils are used. Two are wound on the yokes and two on the
pole pieces clamped to the specimen (see Fig. 22). The induction is measured in the usual
way with a coil wound around the center of the sample. A small rotatable H coil is ar-
ranged so that readings can be taken at different distances from the surface of the sample*
the data so obtained give a curve of the variation in H and indicate by extrapolation the
true value of field at the center of the sample.
In practice, magnetic materials are often subjected to alternating fields, and it is, there-
fore, important to measure magnetic permeability and energy losses by a-c methods
These Delude the use of a-c bridges, wattmeters, cathode-ray oscilloscopes, and various
other instruments, a few of which will be described.
MEASUREMENT OF MAGNETIC CHARACTERISTICS 2-75
One of the common bridge circuits is the Maxwell bridge. The simplest form of this
bridge consists of a pair of resistances for ratio arms, a variable resistor and variable in-
ductance to balance the impedance of the sample, and a detector which may be a gal-
vanometer, a sensitive voltmeter, or a telephone receiver (see Fig. 23). The bridge is
useful for measuring apparent permeabilities and losses for low inductions at frequencies
in the audio range. It is not suitable for testing at high inductions because of errors
introduced by wave-form distortion.
FIG. 22. Schematic Diagram of the High-H
Permeameter
FIG. 23. Simplified Maxwell Bridge Circuit for Deter-
mining Equivalent Series Resistance, R, and Induct-
ance, L, of a Coil Containing a Specimen of Magnetic
Material
Incremental or superposed permeability measurements can also be made with the Max-
well bridge, by using an additional winding on the sample connected in series with a large
inductance and a source of direct current. The inductance in the d-c circuit must be
large enough to keep the alternating current in this circuit at a negligible value. Incre-
mental permeability is important in the transformers of vacuum-tube amplifiers and in
polarized apparatus such as telephone receivers where the material is subjected to both
d-c and a-c fields (see Fig. 24) .
REVERSIBLE PERMEABILITY , fJlr
p p — . — w |v
o £• o> to b> b ji
-^
\
\ 45 PERMALLOY
\
VANA
PERME
DIUM
NDUR
A
•\
\
ARMCO IRON
[
—
^,\s^
=JB«
•sx
"0 4 8 13 16 20 24
POLARIZING INDUCTION, B0
FIG. 24. Change in Reversible Permeability with Polarizing Induction for Several Materials
Properties are often determined at frequencies above the audio range with a-c bridges
of the resistor-capacitor type, and Q-meters. For further information on a-c bridge
methods, see Measurement of Inductance and Effective Resistance, Section 11.
For magnetic materials in sheet form, it is convenient to test samples made of sheared
strips. The Epstein test, in common use for testing the core loss of materials such as silicon-
iron sheet, uses samples of this form. Primary and secondary windings are placed on four
hollow square forms mounted in the form of a square. The primary exciting current is
measured with an a-c ammeter, A, and the induction is indicated by an "average" volt-
2-76
PROPERTIES OF MATERIALS
meter sometimes called a flux voltmeter, connected across the secondary as indicated in
Pig. 25. The core loss is determined from the reading of a wattmeter, W. The test strips
used in" the Epstein are usually stacked with overlapping joints for permeability tests but
may be stacked with butt joints for core-loss tests. This method gives reliable data up to
(a)
v OUTER INNER, FORM STRIPS
WINDINGS
FIG. 25. Descriptive Drawing and Simplified Circuit Diagram for the Epstein Test for Determining
Watt Loss
high inductions, and it is particularly useful for studying grain-oriented materials. For
details of this test and other test methods, the latest issue of ASTM specifications should
be consulted.
Cathode-ray oscilloscopes are sometimes used to give rapid indications of the a-c prop-
erties of materials. By means of a simple integrating circuit, hysteresis loops can be
produced on the screen. A simplified circuit of this type is shown in Fig. 26. This test is
SPECIMEN
FIG. 26. Simplified Circuit for Producing Hysteresis Loops on Cathode-ray Screen
not^ as precise as those described above, but because of its rapidity it finds frequent appli-
cation in certain types of production testing.
BIBLIOGRAPHY
Frequency Cores of Hieh Permeability, Electronic Industries,
ASTM Spec. A-34.
L, G. 0., and H. :
>1. 4, 86 (1945).
TH, h.R.M., Present Status of Ferromagnetic Theory, Elec. Eng., Vol. 54, 1251 (1935).
The Physical Basis of Ferromagnetism, Bell Sys. Tech. /., Vol. 19, 1 (1940)
t&rtL-Qj- J^ ariA TUT Vlrt-MTi.* J?«~~^™__ J-- /?_ /~\ . \ '« . ' — V ..','. -
g^ker, R., and W. Doring, Ferromagnetism (in German). Springer, Berlin (1939).
Cioffi, P. P., Eydrogemzed Iron, Phys. Rev., Vol. 39, 363 (1932) \*-™*)-
DiUi^rL.i ?r*'ia?do?n A&oS°aorth' Heat Tr*^nt of Magnetic Materials in j
.. Physics, Vol. 6, 279 (1935).
a Magnetic Field,
BIBLIOGRAPHY 2-77
Electrical Engineering Staff of M. I. T., Magnetic Circuits and Transformers. John Wiley, New York
(1944).
Ellis, W. C., and E. E. Schumacher, A Survey of Magnetic Materials in Relation to Structure, Bell
Sys. Tech. J., Vol. 14, 8 (1935).
Elmen, G. W., Magnetic Alloys of Iron, Nickel and Cobalt, Elec. Eng., Vol. 24, 1292 (1935).
Hornfeck, A. J., and R. F. Edgar, The Output and Optimum Design of Permanent Magnets Subjected
to Demagnetizing Forces, A.I.E.E. Trans., Vol. 50, 1017 (1940).
Legg, V. E., Survey of Magnetic Materials and Applications in Telephone System, Bell Sys. Tech. J.t
Vol. 18, 438 (1939).
Legg, V. E., and F. J. Given, Compressed Powder Molybdenum Permalloy for High Quality Inductance
Coils, Bell Sys. Tech. J., Vol. 19, 385 (1940).
Messkin, W. S., and A. Kussmann, Ferromagnetische Legierungen (in German). Springer, Berlin (1932).
Rotors, H. C., Electromagnetic Devices. John Wiley, New York (1941).
Ruder, W. E., Permanent Magnet Steels, Iron Age, Vol. 157, 65 (1946).
Sanford, R. L., An Apparatus for Magnetic Testing at Magnetizing Forces up to 5000 Oersteds, Bur.
Standards J. Research, Vol. 23 (1939).
Permanent Magnets, Bur. Standards Circ. C448 (1944).
Spooner, T., Properties and Testing of Magnetic Materials. McGraw-Hill, New York (1927).
Woldman, N. E., and R. J. Metzler, Engineering Alloys. Am. Soc. Metals (1945).
Yensen, T. D., Magnetically Soft Materials, Trans. Am. Soc. Metals, Vol. 27, 797 (1937).
SECTION 3
RESISTORS, INDUCTORS, CAPACITORS
RESISTORS AND RHEOSTATS
BY PAUL S. DARNELL AND
ART. ARTHUR H. SCHAPER PAQE
1. General 02
2. Wire- wound Resistors 05
3. Composition Carbon Resistors 11
4. Deposited-carbon Resistors 15
5. Metal Film Resistors 17
6. Potentiometers and Rheostats 17
7. Special-purpose Resistors 21
VARISTORS AND THERMISTORS
BY N. Y. PRIESSMAN
8. Copper-cuprous Oxide Varistor 23
9. Silicon Carbide Varistors 26
10. Thermistors 28
INDUCTORS WITH AIR CORES
BY L. M. HERSHEY
11. Properties of Air-core Inductors 31
12. Electrical Design Considerations 32
ART. PAGE
13. Mechanical Design Considerations 36
14. Inductor Design Formulas 38
FERROUS-CORED INDUCTORS
BY A. J. ROHNER
15. Low-frequency, Sheet-core Inductors ... 42
16. High-frequency, Powdered-core Induc-
tors 50
CAPACITORS
BY JAMES I. CORNELL
17. Classification of Capacitors 53
18. Variable and Adjustable Capacitors .... 55
19. Impregnated-paper Capacitors 60
20. Mica Capacitors 64
21. Ceramic Dielectric Capacitors 67
22. Electrolytic Capacitors 68
3-01
RESISTORS, INDUCTORS, CAPACITORS
RESISTORS AND RHEOSTATS
By Paul S. Darnell and Arthur H. Schaf er
1. GENERAL
DEFINITIONS. A resistor is a circuit element whose primary function is to introduce
electric resistance into an electric circuit.
A rheostat is an adjustable resistor which is provided with mechanical means for changing
its resistance value without opening the circuit in which it may be connected. Its primary
function is to adjust the current in a circuit or portion of a circuit in which it is connected.
It may be in the form of a three-terminal potentiometer as defined below, or it may have
only two terminals.
A potentiometer is defined by American Standards Association as a measuring instrument
by means of which an electromotive force in one of the arms of the circuit may be measured
in terms of one or more other electromotive forces and the constants of the potentiometer
circuit. However, the term potentiometer is most commonly used to refer to any adjust-
able resistor having three terminals, two of which are connected to the ends of the resist-
ance element and the third to a contact which traverses the resistance element without
discontinuity. Its primary function is to convert an impressed voltage into a source of
voltage which can be adjusted from a small percentage of the impressed voltage to approx-
imately the magnitude of the impressed voltage.
PHYSICAL AND ELECTRICAL CONSIDERATIONS. Numerous factors, which will
determine the type as well as the physical size and shape, must be considered in the design
or selection of the proper resistor or rheostat for a specific application. The most important
of these are: (1) resistance value and tolerance; (2) power dissipation under normal and
trouble operating conditions; (3) frequency characteristic, phase angle, and change in
resistance over a frequency range; (4) stability with age and changing conditions of tem-
perature, humidity, and voltage; (5) mounting arrangements — space and shape require-
ments; and (6) relative cost of available resistor structures which will fulfill the circuit
requirements in whole or in part.
Resistance Value. In general two classes of material are used for resistors: (1) pure
metals and metal alloys in which resistance value for any given metal is determined largely
by its physical dimensions, and (2) a composition or mixture of a carbon or metallic con-
ductor with an insulating material in which the resistance value is determined by the
relative proportion of conductor and insulator.
In the first group the element is usually a wire or strip having relatively low resistivity,
which places a definite limitation on the resistance value that can be achieved for a given
volume. The advantages are high stability with age, low temperature coefficient, low
voltage coefficient, and low microphonic noise level. Its disadvantages are relatively high
cost for higher resistance values, corrosion hazard under adverse conditions of voltage and
humidity, limitation on high resistance values, and usually poor frequency characteris-
tics at higher frequencies. Resistance range is normally from about 0.1 ohm to 1 megohm.
In addition to the wire-wound resistors in this class are the metallic or carbon precision
film-type resistors (to be discussed later) which circumvent some of the disadvantages
enumerated here, since they permit attainment of high resistance in small space and have
greatly improved frequency characteristics.
In the second group of resistors, since resistance value becomes a matter of composition
of a mixture, the entire range of resistors in general use (10 ohms to 22 megohms) can be
made in the same physical form and volume, so that size is determined largely by power
dissipation desired. Other advantages are low cost, improved performance at high fre-
quency, and, when wattage is not a factor, small size, light weight, and ease of mounting.
Disadvantages are lesser stability with time, temperature, and humidity compared with
wire-wound resistors, broader manufacturing tolerances, and higher noise level.
A third class of resistors, namely varistors and thermistors (see articles 8 to 10), is
currently finding wide application as special-purpose circuit elements that are character-
ized chiefly by their high sensitivity to temperature and voltage and their relatively high
3-02
GENERAL 3-03
resistivity. In this group the elements consist of semiconductor materials in the range
between metallic conductors and insulating materials.
Resistance Tolerance. The matter of manufacturing tolerance with respect to the
limits of resistance value within which a resistor shall initially be held is important from
the standpoint both of the proper functioning of the circuit involved and of the design of
the resistor itself. Practical tolerances of low-cost resistors commercially available are
of the order of ±5 per cent to ±20 per cent for composition type, and ±1 per cent to
±10 per cent for wire-wound and precision film types.
Of equal importance to the initial manufacturing tolerances is the desired stability of
the resistor during its life. To obtain stability of a lesser order of magnitude than the
original manufacturing limits can be fairly simple at even the closest limits of the ranges
indicated above but will probably become the major problem or even an impossibility for
units adjusted to initial tolerances of one-quarter to one-tenth of those figures, for example.
ENERGY DISSIPATION—TEMPERATURE RISE— POWER RATINGS. Since nor-
mally the total electrical energy supplied to a resistor is dissipated in the form of heat,
the resultant temperature rise will, under adverse conditions, constitute a potential
hazard both to the resistor itself and to the materials of surrounding objects. Industrial
Control Standards (NEMA, July 1, 1946, IC4-22) state that the temperature rise for bare
resistive conductors shall not exceed 375 deg cent as measured by a thermocouple in con-
tact with the hottest spot on the bare conductor, and for resistive conductors imbedded
shall not exceed 300 deg cent as measured by a thermocouple in contact with the hottest
spot on the surface of the imbedding material. The establishment of such maximum power
ratings is possible only for power-type resistors constructed entirely of inorganic materials
not adversely affected either physically or chemically by the heat generated. Ratings
for other resistors are normally established on the basis of the maximum temperature at
which they can operate continuously without deterioration of their performance or their
component parts. Since power ratings under the various standards are predicated on
operation in still air and free space at an ambient temperature of the order of 25 deg cent, a
status seldom realized under actual operating conditions, good engineering practice dictates
derating the resistor to reflect the specific conditions of use. In the absence of exact data
to indicate the amount of derating necessary, a figure of 50 per cent is commonly applied.
In addition to consideration of the normal wattage at which the resistor will be required
to operate, it is frequently advisable to determine the power the resistor must dissipate
under predictable abnormal or trouble conditions, and when possible, to select a resistor
that will operate safely under such conditions as well.
FREQUENCY CHARACTERISTIC. In considering the behavior of a resistor over a
frequency range, it must be remembered that in any practical design in which the element
has finite dimensions it will necessarily contain components
of all three parameters (Fig. 1 — R, L, and C) and will
approach the characteristics of a pure resistor over a limited — ?— vWW — ^^fi^ — j — •
frequency range. The problem of design is to approach a
pure resistance with the inductance and capacitance re- ' |[ I
garded as parasitic values, useful only to the extent to Q
which they can be made to nullify each other over the ~ , ,., . , . ,T . , ,
, . i. r jr -J.-J.T- j A FIG. 1. Equivalent Network of
frequency range in which the resistor is to be used. A a Resistor Having Inductance
typical resistor may be represented as a two-terminal net- and Distributed Capacitance
work comprising three elements as shown in Fig. 1.
The impedance Z of this circuit may be expressed in terms of effective inductance L'
and effective resistance R' of the system as follows: Z = R' + juL'. It can readily be
shown that in terms R, L, and C the following relations hold :
7?/ . ?L m
1 - co2C(2L - CR2) +
L-CR2-
1 - a?C"(ZL - CR2) + oj^L2 (2)
Also the phase angle & = tan^oxLY-SIOr from which
Tan*=a(L-C^-'°2CL2)
Since in a resistor both L and C are small, eqs. (1), (2), and (3) may be rewritten:
Rf = B[l + co2C(2L - CR2)] (4)
L' - L - CR2 (5)
Tan $ =
3-04 RESISTORS, INDUCTORS, CAPACITORS
It will be observed that the phase angle will be zero if L — CW- — 0, but that the change
in resistance will be zero only if C = 0 or if 2L - CR2 = 0. It follows then that both the
phase angle and the change in resistance with frequency can be zero simultaneously only
for the conditions C — 0, L - 0. These are important relations, for it means that a
resistor may be designed with a small or zero phase angle over a considerable frequency
range merely by keeping to a minimum the quantities L/R and CR and making them as
nearly equal as is warranted for the particular design under consideration.
A second factor causing change of resistance with frequency is the so-called skin effect,
which arises from the fact that elements or filaments of current at different points in the
cross-section of the conductor encounter different components of inductance. This is
because of the greater mutual inductance between elements at the center of the conductor.
These unequal inductances over the cross-section tend to produce unequal current densities,
with the minimum at the axis and the maximum at the periphery. Such unequal current
densities reduce the effective cross-section of the conductor and tend to increase its effective
resistance. Since the determination of skin effect by computation is involved, it is suffi-
cient to observe that this effect may be kept to the minimum by (1) using a conductor of
small cross-section, (2) using a conductor of high specific resistance, and (3) for a wire-
Tvound resistor, winding the wire to have the nainimum effective inductance. It will be
seen that these are also conditions for other good characteristics in an alternating-current
resistor. (For a more detailed description of skin effect and methods of computation, see
National Bureau of Standards Circular 74.)
Small Phase Angle over a Frequency Range. As stated previously, to insure small phase
angle over a given frequency range requires that residual inductance and capacitance be
held to the minimum, zero phase angle being realized when one is made to compensate
the other, Such compensation is achieved by satisfying the equation L — CR*. The
major problem for low resistance is the reduction of inductance; for high resistance it is
the reduction of capacitance. In actual practice it is found that for values up to about
100 ohms the problem is one of inductance; for values over several thousand ohms the
problem is mostly capacitance; for values in between, both capacitance and inductance
must be considered. Of course these figures show merely the broad boundaries, and con-
siderable variation will be encountered due to differences in structure, type of winding,
and capacitance to ground.
STABILITY "WITH AGE, TEMPERATURE, AND HUMIDITY. Aging may be defined
as any permanent change in resistance value with time, measured under the same condi-
tions of temperature and humidity. It is generally caused by strains set up in the resistor
element, either in the original manufacturing process as when wire is wound tightly on a
core or when the element is pressed or molded into shape, or during the life of the unit
when the supporting structure is distorted as the result of aging of the structure itself.
In a composition resistor it is also brought about by chemical and physical changes in the
materials of composition, particularly in the deterioration of the insulating materials used
in the binder and filler. Strains in the winding may often be relieved by a preaging treat-
ment (generally baking from 1 to 24 hours). To prevent warpage of the structure, and
to guard against other effects discussed later, resistors are protected against moisture in
various ways. Impregnation with wax, varnish, or asphalt compounds is common practice,
and frequently an exterior covering of moisture-resistant material is used. Proper selec-
tion of structural materials is probably the most important single factor in aging protection.
Metal, which appears to be the ideal material for this purpose, usually cannot be used,
partly because of its effect on the residuals, and partly because proximity to the winding
would be an added hazard in promoting electrolytic corrosion.
Temperature Variations. Stability with change in temperature is obtained by a proper
selection of the resistive material. For composition-type resistors this material is at present
limited almost entirely to carbon or graphite for the conducting portion of the mix; a
wide variety of insulating materials is used for binder and filler, and frequently the choice
is controlled by considerations other than temperature coefficient. For wire-wound resis-
tors the desired temperature characteristics are determined largely by the wire selected.
Humidity Conditions. In addition to warping of structural materials two other humidity
effects must be considered in resistance design: the effect on residual inductance and
capacitance, and the effect on corrosion. When moisture gets into a resistance structure
it causes a change in the dielectric properties of the materials used therein, and a conse-
quent change in the residual capacitance. This will often change the phase angle by an
appreciable amount. The danger of corrosion which takes place when impurities and
moisture are present is generally the more serious consideration in protection against
humidity, especially where fine wires are used.
CLASSIFICATIONS. Resistors have been variously classified in terms of performance,
power dissipation, structure, usage, and manufacturing tolerances. Broadly, the following
WIRE-WOUND RESISTORS
3-05
classifications are in general use today and have been adopted, with proper subdivisions,
by the various standards agencies: (1) fixed wire-wound, (2) fixed composition type,
(3) precision film type, (4) rheostats and potentiometers (wire-wound and composition),
(5) special-purpose types (chiefly thermistors and varistors). Each of these categories
will be treated separately below.
RESISTOR TESTS AND SPECIFICATIONS. Aside from a marked quality improve-
ment of the resistor product, one of the major benefits derived from the past war was the
promulgation and adoption by the armed services, and to a lesser extent by industry, of
resistor standards of performance, size, resistance value, and tolerance. These can be
found by reference to the following specifications:
JAN-R-11 Resistors, Fixed Composition.
JAN-R-26 Resistors, Fixed Wire- Wound, Power Type.
JAN-R-93 Resistors, Accurate, Fixed, Wire-Wound.
JAN-R-184 Resistors, Fixed, Wire- Wound (Low-power).
JAN-R-22 Rheostats, Wire- Wound, Power Type.
JAN-R-19 Resistors, Variable, Wire-Wound (Low Operating Temperature).
Specifications include tests of both mechanical and electrical qualities, including meas-
urement of strength of leads, strength of resistor, resistance load life, load characteristics,
voltage characteristic, temperature coefficient, microphonic noise, and effects of humidity,
overload, and aging. In addition the Radio Manufacturers Association is in the process
of preparing corresponding specifications for commercial usage, less severe and exacting.
(See also Section 11.)
2. WIRE-WOUND RESISTORS
The many varieties of wire-wound resistors in use are classified in numerous ways,
some by the manufacturer and some by the application to which the resistor is put. Thus
we have power type, high-frequency resistors, precision type, flat type, tubular, plate,
ballast, cord type, lead mounting, ferrule type, spool type, sectionalized bobbin type, and
many others. As might be expected there is a great deal of overlapping in categories, and
the descriptive terms are of course relative and at times misleading. Wire-wound resistors
will be arbitrarily subdivided here into the several main classifications currently accepted
by most manufacturers and users.
POWER-TYPE RESISTORS. Power resistors consist of that class of resistor whose
primary function is to dissipate relatively large amounts of power in a comparatively
small space. In this group, materials of construction are selected first because of their
ability to withstand heat. Normally temperature rise is limited to 300 deg cent which
with 25 deg cent ambient means a hot-spot temperature of 325 deg cent. Where organic
materials are used (usually to obtain increased resistance to humidity or to facilitate
construction of special features requiring machined or molded parts) temperature rise is
limited to 125 deg cent and wattage
ratings are reduced to about one-third
of maximum values obtainable with com-
plete inorganic construction. Typical
construction consists of a cylindrical
ceramic-core tube with encircling band
terminals at each end, with a single
inductively wound layer of wire made
of resistance material selected for the
qualities desired. Because of corrosion
hazards and considerations of mechanical
strength, choice of wire size is usually
limited to minimum 0.002-in. diameter
(0.0025 in. in JAN specifications), al-
though most manufacturers will wind
wire down to 0.001 in. or less in diameter
if requested to do so. The resistor wind-
ing is protected against mechanical injury
and the effects of moisture. Electrical insulation is obtained by applying a cover coat of
either vitreous enamel or cement. A typical assortment of sizes commercially available
in this type is shown in Table 1.
Maximum resistance value is based on use of 0.002-in .-diameter wire. With 0.001-in.
wire, values up to eight times these maximum figures may be obtained. Wattage ratings
are based on a permissible 300 deg cent temperature rise. Maximum voltage which may
Table 1. Ratings and Dimensions
Nominal
Ratings,
Range of
Resistance
Approximate Core
Sizes, in.
watts
Values, ohms
Diameter
Length
5
0.5 to 1,600
5/16
1
10
0.3to 5,000
5/16
13/4
20
0.3to 10,000
9/16
2
25
0.3 to 13,000
5/8
2
30
0.5 to 23,000
3/4
3
40
0.6 to 28,000
3/4
31/2
50
0.8 to 40,000
3/4
41/2
75
1.2 to 50,000
4 1/4
115
1.9to 90,000
11/8
61/2
160
2. 6 to 120,000
U/8
81/2
200
3. 6 to 150,000
H/8
101/2
3-06
RESISTORS, INDUCTORS, CAPACITORS
be applied is properly held within about 500 volts per inch of length, subject, of course,
to permissible power dissipation.
Other varieties of power-type resistors include the following: strip type, plaque type,
disk type, plate type, supported ribbon, ferrule or axial terminal, adjustable type,
0.5 i 2
Frequency in megacycles
FIG. 2. Resistance Frequency Characteristics of Several Wire-wound Vitreous Enamel Resistors —
50 Watts, 9/i6 ia. Diameter x 4 in. Core (Courtesy Ohmite Mfg. Co.)
0.5 1 2
Frequency in megacycles
FIG. 3. Reactance Frequency Characteristics of Several Wire-wound Vitreous Enamel Resistors —
50 Watts, 9/16 in- Diameter x 4 in. Core (Courtesy Ohmite Mfg. Co.)
molded type, and those with multiple or tapped windings. The adjustable type has a
lengthwise strip of winding bared down one side of the core tube, and the resistor is
provided with an extra encircling band terminal for clamp-
ing down on and tapping the winding at any point along
its length.
Close-tolerance Resistors. Although usual manufac-
turing tolerances available are either ±5 or ±10 per
cent, closer tolerances down to about ±1 per cent can usu-
ally be obtained at increased cost. Tolerances closer than
1 per cent are not generally furnished in power-type resis-
tors since self-heating frequently changes the resistance
value by at least 1 per cent. In the case of vitreous
enamel resistors the high firing temperatures involved in
applying the protective coating and the consequent resist-
ance changes during manufacture make closer adjustment
impracticable. Sometimes varnishes, lacquers, or asphalt
coatings are substituted for the high-temperature coverings
to facilitate initial adjustment, to permit use of low-tem-
per attire-coefficient wires without loss of desirable charac-
Per cent rated load
»-» K> U>-fkOl<T»-vlOOl0C
OOO OOOOOOOc
^
s^
\j
**"
v^
\
^-
)
\
^
^^
\
r-\
^
^
\
\
\
20
40 60 80 100
Ambient temperature in
degrees centigrade
T?T^ A T>^- +~ T* +• f
JiG. 4. ixesistor Iterating for
High Ambient Temperatures as
Specified in JAN-R-26. Curve teristics brought about through additional heat treatment,
d^Sto£$5££l Cu24e and-to pr°^e furthfr P'"°» ^iaSt weathering in
2 — Nominal rating based on 125 service. Such special coatings may necessitate derating
deg cent temperature rise. as much as SO or 90 per cent.
WIRE-WOUND RESISTORS
3-07
Layer Windings. Power-type resistors are occasionally wound in layers to achieve a
greater range of resistance value. Resistance wire having insulation capable of with-
standing high temperatures as well as
having a high degree of mechanical
strength must be chosen for this type of
resistance winding.
Non-inductive Windings. Many of the
power-type resistors may be obtained with
windings of low inductance. Generally
the Ayrton-Perry winding is used (see de-
scription under "Precision-type Resis-
1400
1300
1200
1100
l 000
2 900
1 800
_0>
» 700
'w
•S 600
| 500
£ 400
300
200
100
2k
^
Pef cent of nominal watts a? sea level
SIO C
o c
\
\.
\
\
\
\
\
S
\
X
^Vl
•v^
3 10,000 20,000 30,(
Altitude in feet above sea level
FIG. 6. Resistor Derating When Operated
Above Sea Level (Courtesy Ward Leonard
Electric Co.)
220
160
120
100
20
I | |
100° C rise curve;
(cpi
0 2 4 6 8 10 12 14 16 18 20 22
Number of resistors in group
FIG. 5. Resistor Derating When Mounted in
Groups. Spacings are centerline to centerline of
resistors mounted horizontally — 11/8 in- diameter
core tubes. All resistors of equal length and power
rating. (Courtesy Ward Leonard Electric Co.)
tors"), which has the added advantage of low distributed capacitance and greatly in-
creases the frequency range over which the resistor can be used effectively, particularly
for low resistance values (up to about 10,000 ohms). Figures 2 and 3 show plots of the
normalized effective series resistance and normalized effective series reactance against
frequency for both standard and non-induc-
tive (Ayrton-Perry) windings on 50-watt core
sizes for resistance values of 100, 1000, 5000
ohms, and are representative of the improved
performance that may be expected from this
type of winding. Normalized resistance or
reactance is to be considered as the ratio of
resistance or reactance to the d-c resistance of
the resistor.
Typical behavior and characteristics of some
power-type resistors are shown in Figs. 4 to 10.
Figures 4 to 7 show the required derating of
resistors operated under unfavorable condi-
tions; Figs. 8, 9, and 10 show behavior under
overload and intermittent duty.
LOW-POWER AND PRECISION-TYPE
RESISTORS. This category is made up of
those resistors in which power dissipation is a
minor consideration; it comprises a wide va-
riety of shapes and sizes. Since power dissipa-
tion is not an important factor, many more ma-
terials are available for body structures and
protective coatings, including plastics and
molding compounds, which are more readily
adaptable to the form of unit required.
Precision resistors fall within this category
and are Usually considered to be resistors which
are manufactured to tolerances of ±1 per cent
or less and which are stable during their normal
life and operating conditions to within toler-
/250'
ie C rise
W0 10 20 30 40 50 60 70 80 90 100
Watts in per cent of nominal continuous rating
FIG. 7. Temperature Rise of Resistors in
Free Air, and Enclosed in a Metal Box. Unit
mounted in unventilated metal box reaches
maximum permissible .temperature when dis-
sipating only about 60 per cent of normal rat-
ing. (Courtesy Ward Leonard Electric Co.)
3-08
RESISTORS, INDUCTORS, CAPACITORS
300
OL •£ rf <^coi^<£ifl ^
£ \ I / // / I
£100
FIG. 8. Heating Time Required
to Raise" Hot-spot Temperature
300 Deg Cent for 50-watt (9/16
in.x4: in.) Resistor for Overloads
up to 1000 Per Cent of Rated
Load. A 100 per cent load will
bring full 300 deg cent rise in
about 10 minutes. (Courtesy
Ohmite Mfg. Co.)
20
40
60 80 100
Time in seconds
120 140
150
FIG. 9. Heating Time Required to Raise Hot-spot
Temperature 180, 240, and 300 Deg Cent for Over-
loads up to 1000 Per Cent of Rated Load. Based
on rating of 50 watts for 9/ig in. x. 4 in. vitreous
enamel resistor. Will reach 300 deg cent with con-
tinuous operation at rated load. (Courtesy Ohmite
Mfg. Co.)
200 300 400500
Per cent of rated load
1000
1000
900
\
N^
800
X /
V
^J
\.
"° 600
\%
- 500
>
&
s*&
•a DUU
£ 400
^\
\
^
•g wu
*S 300
'tf
%
ft
V
s
ft
«.
" 200
t
\
\
s,
o
a.
100
\
0.5 1 2
Duty cycle in percent
10 20 30 40 50 70 100 200
Maximum permissible heating time in seconds
3 4 5 6 78 10
FIG. 10. Permissible Duty-
cycle for 50-watt (9/ie in. x
4 in.) Resistor Based on a
Maximum Hot-spot Tempera-
ture Rise of 300 Deg Cent.
Curve A — Per cent of rated
load at which resistor may be
operated on intermittent duty.
Curve B — Maximum time re-
sistor may operate during any
one cycle. (Courtesy Ohmite
Mfg. Co.)
WIRE-WOUND RESISTORS
3-09
ances of something less than the initial adjustment, A few of the types in general use
today are the following:
Spool Type, in which the winding is applied to a core body in the form of a spool, either
molded or fabricated, to the dimensions necessary to accommodate sufficient wire for
maximum resistance value desired and to dissipate rated watts with the minimum of
self-heating. The spool may be divided into sections to control the voltage gradient
between individual turns and between sections of winding and to permit some improve-
ment in frequency characteristic over a winding applied in a single section. Typical sizes
available are shown in the tabulation.
Spool Dimensions,
in.
Watts
Rating
Maximum Resistance
Value, megohms
Minimum 0.0015
in.-diameter Wire
Diameter
Length
19/32
19/32
25/32
19/32
H/32
19/32
0.5
0.75
1.0
0.15
0.4
1.0
Flat-type resistors (card-type) usually consist of a single layer of bare or insulated wire,
wound on a flat card of insulating material. The wound card is either encased in molding
compound or is given a protective coating of lacquer or varnish. Maximum resistance
value is typically of the order of 5000 ohms per inch of length and wattage dissipation
about 1 watt per square
inch of radiating surface. Table 2. Net Residuals of Typical Resistor Windings
Pad-type resistors con-
sist of multiple windings
on a spool or card to form
resistor networks suitable
for use as attenuators.
Plug-in type resistors
are provided with termi-
nations at one end in the
form of a vacuum-tube
base, providing means for
inserting attenuator pads
in a circuit.
Flexible resistors are
made in the form of a helix
wound on a flexible insu-
lating cord which in turn
is insulated with a flexible
sleeving.
WINDING TYPES.
Numerous types of wind-
ing are commonly used in
resistors in an effort to at-
tain low residuals of ca-
pacitance and inductance
or simply to achieve the
desired resistance value in
the most economical way.
Some of these winding
types are shown here.
Typical residuals obtained
are shown in Table 2.
Continuous Winding.
The simplest of all wind-
ings is one in which the
wire is wound on a core
continuously in one direc-
tion, known generally as a
continuous or inductive
winding. If the wire is wound in layers, the residuals of both capacitance and inductance
are large and the resistor can be used merely for very low frequencies or direct-current
applications. By winding in a single layer on a core of small cross-sectional area such as a
Winding Type
Resistance,
ohms
Approximate
Net Residual
Continuous (flat-card type)
0-4.5
4.5-20
20-600
1,000
10,000
0-1. 5 ith
0.5-3. 5 /ih
3.5-15/xh
70 Mh
±3Mjuf
Continuous (tubular power type)
0- 200
200- 800
800-2,000
2,000-5,000
2-1 5 ^h
15-60 juh
60- 130 jit
1 30-500 /*h
Bifilar
10
100
1,000
3,500
0.5 Mb
1.5Mb
100 MM£
300 wif
Reverse layer
1,000
3,500
10,000
10 wrf
30/tMf
lOOwtf
Reverse section
1,000
3,500
10,000
100 A*h
300 juh
±5 jtt/xf
Reverse half-section
1,000
3,500
10,000
d=5wrf
±5 /i/rf
30 ftfd
Mandrelated filament
'1,000
3,500
10,000
35,000
100,000
200,000
1-2 «rf
1-2 w£
1-3 wd
2-4 wf
2-5 «uf
3-8 w*f
Parallel opposing (Ayrton-Perry)
100
1,000
10,000
0-1 Mh
1-2 /*h
1-2 pid
3-10
RESISTORS, INDUCTORS, CAPACITORS
flat card or small-diameter core, the inductance and capacitance are reduced. By spacing
the turns and keeping the wire size to the minimum almost any desired residual may be
achieved with the obvious limitation that short lengths of wire become increasingly difficult
to adjust.
Bifilar Winding. This winding is used most generally where low inductance is required.
In this winding the wire is bent back on itself at the midpoint so that the two half-lengths
are side by side, separated by the insulation only. In this straight form any given wire
has the minimum possible inductance. This minimum inductance L may be computed
from the formula :
L = 0.005Z(2.303 logio ^r + 0.25) ph
Loop or splice
at midpoint tied
down to core
where I — total length of wire in inches, D — distance apart, between centers, d = diam-
eter of the bare wire, and juh = microhenries. D and d are expressed in the same units.
In practice this loop is generally wound on a core (see Fig. 11),
often in several layers, with the result that L is increased slightly.
Spool The bifilar winding has the disadvantage of high distributed capac-
itance. Next to a straight inductive winding, it is the cheapest
winding to apply.
A modification of the straight bifilar winding is the series-bifilar
winding in which the total length of wire is divided into sections,
each wound separately as a bifilar loop and the sections connected
in series. This has the advantage of maintaining minimum induct-
ance and of reducing the capacitance by any desired amount,
inasmuch as the capacitance is approximately inversely propor-
tional to the square of the number of sections. This results in
a good resistor, but it is expensive to apply, and since simpler
windings generally give practically the same results it is seldom
used in regular production.
Reverse Layer Winding. The reverse layer winding (see Fig. 12) is used where the
frequency range is low enough to permit appreciable residuals and where the spool is not
divided into sections for a sectional winding. The direction of turns is reversed for each
layer. It approximates the series-bifilar winding, but, because each layer must be secured
in place before reversing turns, it is expensive where a large number of layers are applied.
To be non-inductive it must have an even number of full as well as partial layers.
Spool^
Two wires wound
together in parallel
for one or more layers
FIG. 11.
Bifilar Wind-
ing*
-
Section through winding on
center line of spool
Notes:
1. Section shows alternate fufl
layers and finaJ partial layers
wound in opposite dlrectians-
O indicates layer wound
towards observer. 0 indicates
layer wound away from obser*
ver.
2. Winding always consists of
even number of fuU and
partial layers.
FIG. 12. Reverse Layer Winding
m
~^~-~, .-^.w* ..JJ
B 111 mi
Section through winding on center line of spool
Notes:
1. © indicates section of winding wound toward the
observer.
« indicates section of winding wound away from
observer.
2. Approximately the same numberof turns are wound
in each of the sections.
3* Figures indicate winding order.
FIG. 13. Reverse Section Winding
Reverse Section Winding. The reverse section winding (see Fig. 13) is used largely
for high resistance values. This winding is divided into two or more adjacent sections of
equal size and number of turns. As in the series-bifilar winding, the distributed capacitance
is approximately inversely proportional to the square of the number of sections. The
turns in adjacent sections are wound in opposite directions to reduce the inductance,
thereby approximating the reversed layers of a reverse layer winding. Generally the spool
is sectionalized to simplify the winding. However, if the wire is large and the turns cor-
respondingly few, the same effect is attained in a bunch-type winding in which the wire
is wound in successive bunches around the core.
Reverse Half-section Winding. Although the reversed section winding gives excellent
results for capacitance reduction, the magnetic coupling between adjacent sections is so
COMPOSITION CARBON RESISTORS 3-11
low that in spite of reverse turns the inductance is often too high. This is especially true
for values ranging from 1000 to 4000 ohms. Although above this upper limit high residual
inductance still obtains, tolerable phase angle results because of the increasing effect of
higher resistance value in the L — CRZ relationship of eq. (6) . Reversing by half -sections
has the effect of increasing the capacitive and decreasing the inductive residuals. This
winding is somewhat more expensive to apply than the reverse section type.
Parallel Opposing (Ayrton-Perry) Winding (See Fig. 14). This type of winding consists
of two inductive windings on a core with turns equal and in opposite direction. A spaced
layer of either insulated or bare wire is first applied in one direction. The second wire is
wound in the opposite direction between the turns of the first winding. When bare wire
is used, the cross-overs must be at Tocommon
exactly diametrically opposite Sides Of terminal Crossovers (pomts of equal potential on each wire)
the core so that contact occurs at \
points of equal potential on each wire. /^-^\ Y
The two windings are connected in
parallel. The distributed capacitance
is low, and the opposing currents in
the two wires produce the minimum " N^ To cornrn'OQ
Of magnetic effect. It has the dis- Two wires wound on core in smgje layer in terminal
advantage of requiring four times as ^^SH^^S'" tim
much wire of any given size to obtain circumference
the same value produced from a nor- FlQ> M> ParaUel Opposing (Ayrton-Perry) Winding
mal single-wire winding.
Mandrelated Filament Winding. This is an adaptation of the continuous winding dis-
cussed earlier, in which a single layer of resistance wire is wound on a flexible core. The
helical filament so formed can then be handled in much the same manner as ordinary
resistance wire. A number of such filaments have been developed with resistance wire,
dimensions, and turn spacing so selected that for any straight length of filament the in-
ductive component L/R is substantially equal to the capacitive component CR. The
effect of winding on a form and terminating the filament is to increase the capacitance
slightly. Because of the excellent frequency characteristics and the high resistance per
linear length of filament (up to 2400 ohms per inch in 0.030-in. diameter of insulated
filament), this type of winding is widely used for high resistance values in many of the
designs developed for use in the communications field.
Miscellaneous Windings. Numerous other windings have been developed for use at
high frequency that serve satisfactorily but are not in general commercial use except in
precision-type measuring apparatus and in resistance standards. One of these is the
"woven type" in which wire is woven into a cloth or ribbon pattern giving the effect of a
continuous winding on a card of infinitesimal thickness. Rather intricate patterns are
sometimes used to obtain low phase angle. Constructions such as "reversed turn" and
"Curtis" windings require handling of each turn individually and therefore do not lend
themselves to economic manufacture in mass production. Occasionally zero phase angle
is achieved by adding the necessary amount of capacitance or inductance to a completely
wound unit.
3. COMPOSITION CARBON RESISTORS
FIXED RESISTANCE RESISTORS. The designation "composition resistor" denotes
a type of resistor that has very wide application in electronic equipment and apparatus
because of its light weight, compactness, wide range of resistance values covered, and ease
of mounting. It is primarily used in circuits where drift and variation in resistance value
with time, temperature, humidity, and applied voltage are not of particular significance.
In general, the resistive element in a composition resistor is a combination of finely divided
carbon or graphite, a non-conducting inert material or filler such as talc, with synthetic
resin as a binder. These substances are proportioned so as to yield the proper resistance
value in the finished product.
|l Composition resistors are available in insulated and non-insulated types. In general,
the large majority of composition resistors used in electronic equipment is of the insulated
type. In this type the resistive element of the unit is surrounded by a substantial housing
of insulating material, such as mineral-filled Bakelite, so that there is no possibility of
contact with the element other than through the wire terminal leads of the resistor.
The usual form of insulated resistors for wattage dissipations of 2 watts and less is a
cylindrical body provided with axial terminals. In the uninsulated resistor, a cylin-
drical rod of resistive material is generally equipped with radial leads and the unit is
painted.
3-12
RESISTORS, INDUCTORS, CAPACITORS
SIZES AND RATINGS. Typical sizes in general usage of fixed insulated axial lead
resistors with cylindrical bodies are as listed in Table 3.
Table 3. Sizes of Cylindrical Insulated Resistors
Nominal
Wattage
Rating
at 40° C
Maximum
Body
Length,
in.
Maximum
Body
Diameter,
in.
Lead
Length,
in.
Min. Lead
Diameter,
in.
0.25
0.50
1.0
2.0
0.438
0.438
0.750
0.750
0.125
0.156
0.280
0.344
1 V2 ± VS
1 V2 ± VS
1 1/2 ± 1/8
1 1/2 =fc 1/8
0.028
0.028
0.032
0.036
The resistors listed in Table 3 are available in resistance values ranging ^ from a few
ohms to 22 megohms on a manufacturer's standard basis, with the qualification that the
:. Nominal Resistance Values
(RMA preferred number system)
low as for the other units.
These resistors are fur-
nished in accordance with
the RMA preferred num-
ber system for the values
and tolerances shown in
Table 4.
jmber of zeros or
decimal multiplier
, ,
I 2nd ) significant
' 1st 3
figures
FIG. 15. Standard Color Cod-
ing
The resistance value is
indicated by a color code
applied to the resistor as
shown in Figs. 15 and 16
and Table 5. The exterior
body color of insulated re-
sistors may be any color
except black. It is recom-
mended that the maxi-
mum continuous working
voltage, either d-c or rms
volts for the 0.5-watt unit;
Nominal Resistance
Available in
Tolerances
± per cent
ohms
megohms
10
100
,000
10,000
0.10, .0, 10
5, 10, 20
n
110
,100
11,000
0.11, .1, 11
5
12
120
,200
12,000
0.12, .2, 12
5, 10
13
130
,300
13,000
0.13, .3, 13
5a
15
150
,500
15,000
0.15, .5, 15
5, 10, 20
16
160
,600
16,000
0.16, .6, 16
5
18
180
,800
18,000
0.18, .8, 18
5, 10
20
200
2,000
20,000
0.20, 2.0, 20
5
22
220
2,200
22,000
0.22, 2.2, 22
5, 10, 20
24
240
2,400
24,000
0.24, 2.4
5
27
270
2,700
27,000
0.27, 2.7
5, 10
30
300
3,000
30,000
0.30, 3.0
5
33
330
3,300
33,000
0.33, 3.3
5, 10, 20
36
360
3,600
36,000
0.36, 3.6
5
39
390
3,900
39,000
0.39, 3.9
5, 10
43
430
4,300
43,000
0.43, 4.3
5
47
470
4,700
47,000
0.47, 4.7
5, 10, 20
51
510
5,100
51,000
0.51, 5.1
5
56
560
5,600
56,000
0.56,5.6
5, 10
62
620
6,200
62,000
0.62, 6.2
5
68
680
6,800
68,000
0.68, 6.8
5, 10, 20
75
750
7,500
75,000
0.75, 7.5
5
82
820
8,200
82,000
0.82, 8.2
5, 10
91
910
9,100
91,000
0.91, 9.1
5
a-c, should not exceed 250 volts for the 0.25- watt unit; 350
and 500 volts for the 1- and 2-watt units.
Table 5. Color Code
Color
Figure or
Number of
Zeros
Decimal
Multiplier
Tolerance,
per cent
Black
0
Brown
1
Red ...
2
Orange
3
Yellow
4
Green
5
Blue
6
Violet
7
Gray
8
White
9
Gold .. . .
0.10
± 5
Silver
0.01
±10
No color
±20
Tolerance
Significant
f igu res
FIG. 16. Alternate Color Cod-
ing for Radial-lead Resistors
COMPOSITION CARBON RESISTOKS
3-13
PERFORMANCE CHARACTERISTICS. In addition to obvious requirements on the
mechanical properties of a resistor, such as ruggedness, security of terminals, legibility of
color code, and its d-c resistance value and tolerance as established by a suitable d-c
resistance measurement, the following properties are of interest for commercial uses.
Resistance-temperature Characteristic. Table 6 indicates the range within which an
insulated composition resistor may be expected to vary at the temperatures indicated.
Table 6. Insulated Composition Resistor Variations Due to Temperature
Nominal Resistance Value
Maximum Per Cent Change in Resistance from Value at
Ambient Temperature of +25 ° C
To -15°C
Ambient
To - 55° C
Ambient
To +65°C
Ambient
To +105°C
Ambient
10 ohms to 1000 ohms
-0, +3.5
-0, +5
-0, +6.5
-0, +10
-0, + 6.5
-0, +10
-0, +13
-0, +20
±3
±4.5
±4.5
±5
±5
±8.5
±8.5
±10
1010 ohms to 10 000 ohms
1 0 1 00 ohms to 0. 1 megohm
Over 0. 1 megohm
Voltage Coefficient. This coefficient relates to the percentage change in resistance value
per unit change in voltage with applied voltage as distinguished from any effects caused
by heating at the applied voltage. It arises from a change in the conducting properties
of the resistive material as the applied voltage is varied. Voltage coefficient is usually
determined for resistors of 1000 ohms and above as follows:
Voltage coefficient (per cent) = 100 — ^-=r — - X -= =-
where E\ — rated continuous working voltage, Bz ~ 0.1 rated continuous working voltage,
jRi = resistance at rated continuous working voltage, and Rz — resistance at 0.1 continuous
working voltage. For resistors rated at 1/4 and 1/2 watt, the voltage coefficient should
not exceed 0.035 per cent per volt, and for higher-wattage resistors it should not exceed
0.02 per cent per volt.
Humidity Effects. Test data indicate that molded-housing-type insulated resistors
which have been thoroughly dried and then subjected to a condition of 90 per cent relative
humidity at an ambient of 30 deg cent for 200 hours may in general be expected to stay
within a limit of about 5 per cent, the magnitude of the change depending upon resistance
value. The product of certain manufacturers is also capable of withstanding exposure to
100 per cent relative humidity at an ambient temperature of 66 deg cent for 250 hours
without changing ha resistance value by more than 10 per cent.
Noise. Current noise arises within the resistive element of a composition resistor pri-
marily because of the microphonic nature of particle-to-particle conduction of current
in the structure. In some resistors noise may also
originate at the junction between the lead wire and
resistive element because of imperfect contact.
It has been found that the product of certain
manufacturers will have root-mean-square values
of current noise with rated d-c voltage applied
to the resistor terminals less than 3 rms micro-
volts per volt for 1/2-watt units up to a resistance
value of 1 megohm, and 6 rms microvolts per volt
for resistance values above 1 megohm. For 1-
and 2-watt resistors, the noise level may be ex-
pected not to exceed 1.2 rms microvolts per volt.
Load-life Characteristic. D-c load tests con-
ducted at 40 deg cent have shown such extremely
wide variations in resistance change in 1000
hours that no general statement is of value.
Units have been found to age either positively
or negatively, the film-type resistor usually show-
ing an increase in value and the body type a
decrease in value. Hence the manufacturer
should be consulted for specific information on
the performance of his product. However, resistors are available which will not change
more than 10 per cent under this 1000-hour load test.
For resistors designed to carry 100 per cent of rated load at 40 deg cent ambient, it is
recommended that the derating curve shown in Fig. 17 be followed to prevent undue aging.
UO
100
90
' 70
n- 30
20
10
\
0 10 20 30 40 50 60 70 SO 90100110
Ambient temperature in degrees centigrade
FIG. 17. Derating Curve for High Ambient
Temperatures
3-14
RESISTORS, INDUCTORS, CAPACITORS
It will be noted, for example, that resistors functioning in an ambient of 85 deg cent should
be operated at not more than 25 per cent of rated load. Resistors are also available which
may be operated at full wattage at 70 deg cent with a derating to zero wattage at 150 deg
cent.
Effect of Soldering. Care must always be taken to prevent the quality of a composition
resistor from being seriously impaired and its resistance value and stability affected sig-
nificantly by excessive heating during the operation of soldering its terminal leads to
apparatus or equipment terminals. The leads should be left as long as possible and prefer-
ably not less than 3/8 in.
Additional Characteristics. In addition to the properties and tests described above,
other characteristics of interest in military work and of possible importance in certain
commercial application may be mentioned: voltage breakdown strength of the insulation
on insulated-type resistors; high-altitude flashover voltage; performance after salt-water-
immersion cycling; effects of thermal shock under temperature cycling in air; effect of
mechanical vibration on mounted resistors; performance under other types of load-life
tests; short-time overload performance; and ability to withstand specific mechanical tests
on the security of terminals. Further details on tests and expected performance may be
found in Specification JAN-R-11.
FREQUENCY CHARACTERISTIC. In general the inductance associated with com-
position resistors is sufficiently small to be disregarded. At low frequencies the value of
resistance R is the same as the d-c resistance, but as the operating frequency is raised the
value of R starts to decrease and may reach a value which is only a few per cent of the d-c
value. The frequency at which R begins to show a significant decrease in value depends
upon its d-c value; that is, the greater the d-c value of a resistor, the lower the frequency
at which departure from the d-c value is observed. Incidentally, parallel capacitance C
shows a similar decline in value, but the amount of change is significantly less than the
reduction in resistance.
Figure 18 shows the variation in resistance with frequency of two different 1-megohm
insulated resistors of i/a-watt rating. These resistors are practically identical in physical
size, but one has a resistive
element in the form of a
composition film on the sur-
face of a glass tube and the
other has a resistive element
of the body type. Resistors
that have been found to
show the least decrease with
frequency have a very thin
uniform resistive film on a
rod or tube of low-loss di-
electric material in which
the ratio of length of ele-
ment to its diameter is large
and in which no exterior
covering or coating material
is in contact with the sur-
face of the element.
It has been observed that, in a given specific type of resistor, the ratio of parallel a-c
resistance to the d-c resistance is approximately constant for a fixed value of the product
of operating frequency and d-c resistance value. That is to say the ratio is approximately
the same for a 10-megohm unit operating at 0.1 me, a 1-megohm unit at 1 me, and a 0.1-
megohm unit at 10 me. In each instance the product of megohms and megacycles is
unity. Applying this example to the curve given for the body-type resistor in Fig. 18,
and noting that at 1 me the 1-megohm resistor has 53 per cent of its d-c resistance, a
resistor having a value of 10 megohms (d-c) and being of the same construction as the
1-megohm unit for which the curve is drawn would have a parallel resistance of around
5.3 megohms at 0.1 me. Also a 0.1-megohm unit (d-c) at 10 me would have a value of
about 53,000 ohms parallel resistance. It is very important to observe that this relation-
ship is only approximate and also must be established for each specific type of resistor.*
This is evident from the fact that, for a product of unity for the film type of resistor shown,
the parallel resistance is about 80 per cent of the d-c value, as compared to 53 per cent for
the body-type unit.
Table 7 indicates the approximate frequency at which a 1-megohm resistor will have a
parallel resistance of 0.5 megohm for 0.5-, 1- and 2-watt resistors within the dimensional
limits stated in Table 3. With the product relationship discussed above, the data in Table 7
J 0.9
§0.8
= °'7
tt*0.6
Jo.4
-£ 0.3
Jo.2
<£ 0
••^^
•*-:
-- —
K
c*
ominal rating, % watt
ze, see table 1
c resistance, 1 megpl*
m
Ns
*•-.
>s
X,
^
^
>v
s»s>
^^
X"
%
"\
Vi
4^
X.
\
v^,
*?°n
^
) 2 4 6 10 40 100 400
Kilocycles per second
• 2 34 6 10 20 40 100
Megacycles per second
Frequency
FIG. 18. Variation of Parallel Resistance R with Frequency for 1-
megohm Molded Insulated Housing Type of Resistor
DEPOSITED-CARBON BESISTORS
3-15
may be used to estimate the frequencies at which other resistors of the same size and type
will drop to values of parallel resistance equal to half of the d-c resistance.
The parallel capacitance C associated with these resistors is also a function of resistor
construction, resistance value, and frequency. Considerable variation in capacitance
value for different samples of the same type has been noted, but the value appears to be
in the order of 1 to 3 ;Ujuf, falling with frequency to around 0.5 to 1 Mjuf.
HIGH-FREQUENCY AND HIGH-VOLTAGE TYPES. Another line of composition-
type resistors is available which is designed for high-voltage and high-frequency applica-
tions. These have various wattage ratings
Table
7. Resistance-frequency Character-
istics of Specific Resistors
1 -megohm Resistor
Nominal Wattage
Rating
Frequency in Megacycles
for R of 0.5 Megohm
Film-type
Element
Body-type
Element
0.5
1.0
2.0
20
3.0
1.2
0.8
0.4
from less than 1 watt to about 100 watts.
In general the high-frequency type con-
sists of a continuous film of resistive element
on the surface of a ceramic tube. In size, as
typified by the product of one manufac-
turer, these resistors range from units about
1/8 in. in diameter and lli in. long with wire
lead axial terminals to units about 2 in. in
diameter and 20 in. long overall, including
ferrule terminals. Resistance values of a few
ohms to several megohms are available, de-
pending upon the physical size of the resistor.
High-voltage composition-type resistors are of similar construction to that described
for the high-frequency type, except that the resistive element is usually in the form of a
spiral or ribbon to provide a long conducting path. They are available in sizes ranging
from units 5/l6 in. in diameter and about 2 in. long rated at 2 watts and 7500 volts maxi-
mum, to units 2 in. in diameter and about 20 in. long rated at 150 watts and 100,000 volts
maximum. Resistance values obtainable range from a few thousand ohms to a million
megohms.
4. DEPOSITED-CARBON RESISTORS
GENERAL DESCRIPTION. " Deposited-carbon resistor" denotes a kind of resistor
in which the resistive element is a film of carbon deposited on the surface of a suitable
ceramic core by the thermal decomposition of gaseous hydrocarbons at high temperatures.
This film is extremely thin and by proper control of the coating process may be varied in
thickness within the range from 1 X 10 ~4 to 5 X 10 ~8 in. The resistance of such films
ranges from about 5 ohms per unit square to about 10,000 ohms per unit square. "Ohms
per unit square" denotes the resistance as measured between opposite edges of a square
of resistance film of the thickness indicated.
Electrical connection is made to the carbon film by applying low-resistance electrodes
of either graphitic or special metallic paint. These electrodes are cured by suitable heat
treatment, and then metal caps with integral lead wires are forced over them. Since the
carbon film is sensitive to abrasion and also needs protection from contamination, the
resistance structure is coated with a suitable baking varnish or housed in an enclosure.
Resistors having resistance values up to a few thousand ohms are formed of uniform films.
High-ohmage units are obtained by cutting a helical groove through the carbon film to
form a ribbon of film wound around the core between the end electrodes. The surface
perfection of the ceramic core and its other physical and chemical properties have a marked
effect on the electrical characteristics of the resistor.
USAGE. Deposited-carbon resistors provide exceptional resistance stability and com-
pactness in high values of resistance. Also, because of low residual inductance, the power-
type varieties are of value as load resistors in testing high-frequency equipment. Special
shapes of deposit ed-carbon resistors in the form of suitably terminated small rods and
disks are available for assembly in coaxial-type attenuator units for use in making accurate
attenuation measurements up to frequencies of several hundred megacycles.
SIZES AND RATINGS. Typical figures for the product of one manufacturer are given
in Table 8. These resistors have cylindrical bodies. The resistors with the shell enclosures
have axial leads and are intended for general-purpose use. The glass-enclosed units are
hermetically sealed with an inert gas in the enclosure and are provided with ferrule end
caps as terminals; they are intended for applications in which high stability in resistance
value or high levels of power dissipation are involved.
PERFORMANCE CHARACTERISTICS. The general-purpose resistors and the
glass-enclosed types for high-stability application are available in tolerances as close
as ±1 per cent. The large power dissipating units are available in tolerances of ±5
per cent.
3-16
KESISTORS, INDUCTORS; CAPACITORS
Table 8. Ratings and Sizes of Deposited-carbon Resistors
Rating
Norn,
at 30° C
Wattage,
Maximum *
Approximate Overall
Size, in.
Resistance Range,
ohms
Short-
period
Peak
Voltage f
Protective
Enclosure
Diameter
Length
Minimum
Maximum
0.15
0.5
1.0
1.0
2.0
0.5
1.5
3.0
10
20
60
300
600
H/64
H/32
H/32
7/16
7/16
5/8
11/4
U/4
Wl6
1
2Vl6
21/4
3V4
411/16
83/4
143/4
1
200
200
200
200
20
20
40
5X 106
106
5 X 107
107
1.5 X 10?
10?
5X 106
107
5,000
8,000
15,000
2,000
6,000
10,000
20,000
40,000
Shell
Shell
Shell
Glass
Glass
Glass
Glass
Glass
* At maximum wattage, resistance may differ from 30 deg cent value by decreases of 10 to 15 per cent,
t Not to exceed that required for maxim urn power rating.
Temperature Coefficient. The temperature coefficient of the carbon film depends upon
its thickness and ranges from about — 180 parts per million per degree centigrade for very
heavy coatings to about — 500 parts per million per degree centigrade for light coatings.
Furthermore, the application of protective lacquer to the film may modify its temperature
coefficient by virtue of mechanical effects on the film. The physical properties of the
ceramic base also affect this coefficient. Hence the temperature coefficients of these
resistors range from about —0.02 to possibly —0.10 per cent per degree centigrade, depend-
ing upon resistance value and constructional features. The resistance-temperature curve
is approximately linear over the temperature range of —40 deg cent to +60 deg cent.
Voltage coefficient is in general negligible for deposited-carbon units. Occasionally an
individual resistor may show a slight resistance variation with voltage but probably not
more than 0.002 per cent per volt.
Humidity effects depend upon the structure of the resistor and in hermetically sealed
units become a matter of leakage across the surface of the housing. The following figures
are indicative for general-purpose units with shell enclosures. After exposure to a condition
of 90 per cent relative humidity at an ambient of 30 deg cent for 200 hours, the maximum
change in resistance may be expected to be less than 1 per cent, with an average change
of less than 0.5 per cent.
Noise. At low levels of voltage, deposited-carbon resistors exhibit pure thermal noise,
but as the voltage is raised other electrical noise may be observed. This may be some form
of contact noise due to imperfections or loose contacts in the carbon film. However, at
rated load the noise level, excluding thermal noise, may be expected not to exceed 0.25
rms microvolt per volt.
Load-life Characteristics. General-purpose-type deposited-carbon units when operated
at their normal wattage rating may be expected to show average changes in resistance
value of not more than 1 per cent after 2000 hours. Occasional units may age as much as
1.5 per cent. Hermetically sealed resistors operated at high power levels may show more
rapid aging. For example, the 7/i6 X 3 1/4 unit in Table 8 may change in resistance value
up to 3 per cent after 3000 hours of operation at 10 watts. Load aging may cause either a
positive or negative change in resistance but generally results in a positive change. In
using power-type resistors, care must be taken to insure that the voltage gradient within
the resistor is not sufficient to give rise to corona or cause flashover between adj acent turns
of a spiraled element and thus damage the unit.
Like composition resistors, when deposited-carbon units are operated in high ambient
temperatures they should be derated. For types which are not hermetically sealed, it is
recommended that the maximum operating surface temperature of the carbon film not
exceed 120 deg cent. Since their normal rating is established at 30 deg cent, the wattage
ratings for these units should be decreased by about 1 per cent for each degree centigrade
that the ambient exceeds 30 deg cent. For glass-sealed\mits, which under maximum power
ratings may operate at surface temperatures up to 450 deg cent, the ratings can be re-
garded as independent of ambient temperature up to about 80 deg cent. The manu-
facturer should be consulted for further derating information for the specific conditions
of application. The ratings of power units can be increased several fold by forced air cool-
ing, and, for a-c application, resistors are available which may be liquid cooled through
direct contact of the coolant with the film. Anodic oxidation of the film precludes the
use of water cooling on d-c applications.
The effect of soldering is negligible on lead-type units, provided, of course, that the re-
sistor is not damaged by direct contact with the soldering tool.
POTENTIOMETERS AND RHEOSTATS 3-17
No-load Aging. Under conditions of no-load or shelf-aging, deposited-carbon resistors
of the general-purpose type may be expected to drift in value not more than 0.1 to 0.2
per cent per year. Hermetically sealed units appear to have a stability in resistance value
of the order of 0.005 per cent per year, which is about the limit of error in measurements
extending over such a time period. In fact the stability of high-quality hermetically sealed
carbon film resistors, particularly in the megohm region, appears to be at least as good as,
if not better than, that of equivalent resistance wire-wound units.
FREQUENCY CHARACTERISTIC. Deposited-carbon resistors exhibit a decrease in
parallel resistance with frequency. However, the rate of decrease does not appear to be
as rapid as in the insulated-type composition resistor, and it is less for the glass-enclosed
type than for the varnished or shell-protected unit in which the protecting material is in
contact with or very close to the carbon film. A 1-watt varnish-coated 1-megohm unit,
9/32 in. in diameter and 2 1/16 in. long, drops to 0.5 megohm parallel resistance at about
12 me.
Whereas the inductance of an unspiraled film is negligible, the inductance of a spiraled
unit may be appreciable. For example, the inductance of a 1-megohm resistor of the
7/i e in. X 3 1/4 in. size in Table 8 is about 1.1 microhenries. Though spiraling increases
inductance, the ratio of inductance to resistance remains essentially unchanged. Since
the effects of distributed capacitance are changed only slightly by spiraling, the alteration
in high-frequency behavior of a resistor which is spiraled to a high resistance value is
largely that associated with the resistance increase alone.
5. METAL FILM RESISTORS
These resistors are formed by coating a base of suitable material with a very thin film
of metal or metallic alloy. This film may be applied to the base by cathode sputtering or
metal evaporation processes, and by chemical methods. It is quite thin, being of the order
of 10 ~7 in. thick. The material used for the base may be ceramic, glass, or an organic body
such as Bakelite.
In one construction, a thin film of palladium is deposited by a chemical process on a
ceramic-core tube. The ends of the film are coated with silver or some other metal to
form electrodes for the attachment by soldering of radial lead wires. The film is covered
by a form of vitreous covering to afford protection against oxidation and corrosion as well
as against mechanical damage. High values of resistance are obtained by cutting a helix
through the metal film into the core, in the same fashion as deposited-carbon film resistors
are helixed. For further protection the whole unit, including the portion of the lead wires
in contact with the resistor body, is lacquered. Resistors made in this way are available
over a range of resistance values in several sizes corresponding to different wattage ratings.
They possess good electrical stability under aging and load conditions, and they have good
heat-dissipating properties. As determined from observations on a limited number of
samples with a nominal rating of 1 watt, aging under d-c rated load is predominately
positive as regards resistance value and may be of the order of 1 to 5 per cent after 1000
hours, depending upon resistance value. The temperature coefficient is negative and
varies to some extent with resistance value. It also shows considerable departure from
linearity over the temperature range of —40 deg cent to +80 deg cent. Referred to resist-
ance value at 20 deg cent, resistors increase in value by about 5.5 per cent at — 40 deg cent,
and at 80 deg cent they decrease in value by about 3 per cent.
In another construction of metal film resistor, a resistance alloy such as Nichrome is
evaporated to form a very thin film on the surface of a glass tube or rod. A layer of pro-
tective material is placed over this film, and lead wires are attached in the same general
manner as described above. An advantage of this type of construction is that the low
temperature coefficient of the resistance alloy is retained in the resistor.
6. POTENTIOMETERS AND RHEOSTATS *
Potentiometers and rheostats in general use in the communications and electronics
fields may be classified as wire-wound and composition types. Those most extensively
used are the continuously adjustable type, where a movable contact traverses a resistance-
wire winding or a composition resistance element in small increments of their lengths. In
most instances the movable contact is controlled by a rotatable shaft, although in some
the resistance element is rotated. It is standard practice to have terminals for both ends
* Article 6 was contributed by A. H. Vblz.
3-18
RESISTORS, INDUCTORS, CAPACITORS
100
"40 50 60 70 80 90 100
Ambient temperature In
degrees centigrade
FIG. 19. Power Derating
Curve for Continuous Duty
of the resistance element in addition to a terminal for the movable contact so that they
may be wired either as potentiometers or rheostats.
Most of the potentiometers and rheostats hereinafter described may be obtained in
tandem arrangement either with a common shaft which adjusts each unit simultaneously
or with concentric shafts which permit independent adjustment of the tandem units.
WIRE-WOUND POTENTIOMETERS AND RHEOSTATS. Low-operating-tempera-
ture potentiometers find application as voltage- and current-adjusting devices in low-
energy circuits. The power ratings are based on operation in
free still air at an ambient temperature of 40 deg cent with a
maximum temperature rise of 60 deg cent. A power derating
curve is shown in Fig. 19. When potentiometers are enclosed
and in close proximity to other components it is considered
good practice to limit the power dissipation to about one-half
the rating.
The types that find the widest application are ^ the small
circular potentiometers that range from about 1 1U in. to 2 in.
in diameter and are rated from about 2 to 4 watts. - In this
type bare wire is space wound on a flat strip of insulating mate-
rial, usually a laminated phenolic, which is then formed into
a circular shape and set into a housing or case. ' The contact
shoe or brush is made of a base metal or an alloy of base metals,
supported on a spring member. The force exerted on the
resistance wire by the base-metal contacts usually ranges from
about 100 to 200 grams, sufficient to keep the contact resist-
ance below 1 ohm, providing a satisfactory level of contact
noise for most applications and a useful life of 25,000 to
100,000 cycles of operation. Individual potentiometer designs
may show changes in resistance from 1 to 10 per cent over
the ranges of temperature and humidity usually encountered. *
In general it is desirable to use no smaller than 1.75 mil wire (usually similar to Ni-
chrome), resulting in maximum resistance of about 50,000 ohms for the 2-in. -diameter
size and 10,000 ohms for the 1 1/4-in. size. Standard tolerances on resistance are ±10 per
cent. Closer tolerances and higher resistance values can be obtained on a custom basis-.
Finer wire is more susceptible to wear and electrolytic action.
Various resistance-rotation characteristics are available, the most extensively used
being the linear type wherein the rate of change of resistance between the contact terminal
and one of the end terminals is approximately
constant with angular rotation. In these small
types the degree of linearity is usually of the
order of ±5 per cent of total resistance. This
type of characteristic is illustrated by curve A
of Fig. 20.
For special applications, non-linear or ta-
pered potentiometers can be "obtained. This
non-linear characteristic is effected by chang-
ing the pitch of the winding at certain points
in the range of rotation or by changing wire
size or by a combination of both. Curve B of
Fig. 20 illustrates a clockwise and non-linear
characteristic in which there are two sections
differing in their rates of change of resistance.
As a high percentage of the total resistance
may be concentrated in a small portion of the
resistance element, it is recommended that
non-linear controls be rated at about half of
the rated power of linear controls of the same
designs.
80
60
10
lockwise rotation'
Cur
I
Left
terminal
20 40 50 60 80
Per cent effective rotation
|
100
-TotaJ mechanical rotation —
FIG. 20. Clockwise Tapers
For continuous operation of linear types, the maximum current through the entire re-
sistance element or through any portion thereof should not exceed the value given by the
following equation:
where W is the wattage rating, R is the total resistance, and I is the maximum permissible
current. The maximum current for each section of a non-linear control should be deter-
POTENTIOMETERS AND RHEOSTATS 3-19
mined from the above expression except that R, instead of being the actual total resist-
ance, should be that value which would obtain if the entire resistance element were wound
with the same size wire as the particular section.
There is another group of circular, wire-wound, low-operating-temperature potentiom-
eters which are approximately 3 in. in diameter and range from about 1 1/4 in. to 2 &/8 in.
in depth, and in power rating from 8 to 15 watts. The winding is usually clamped around
a molded phenolic base. This class of potentiometer is usually provided with a winding
of a higher degree of uniformity than the smaller types, owing to the use of higher-precision
winding methods. As a result linearly wound potentiometers are obtainable with linearity
ranging from 1 to 0.3 per cent. Non-linear types are usually produced by shaping the card
or strip on which the wire is wound, which is possible because of the greater depth of the
winding. The amount of taper is limited by the maximum slope (angle between winding
axis and shaped side of card) that can be wound without having the winding collapse
which for close winding is about 40 deg. The deepest linear unit of this group can be wound
to about 200,000 ohms without resorting to Nichrome wire finer than 1.75 mil in diam-
eter. These types are readily obtainable with low-temperature-coenicient wire such as
Advance, which, however, will wear more rapidly than Nichrome since it is softer. An
idea of the performance capabilities of potentiometers of these two groups can be obtained
by referring to the Joint Army-Navy Specification JAN-R-19.
Very special high-precision, low-operating-temperature wire-wound potentiometers
have been developed for military applications. Some of them have winding cards shaped
to provide special resistance-rotation characteristics to an accuracy represented by two
turns of the winding at any point in the range of rotation. Some types have been provided
with closed windings for continuous rotation; in one such type an input d-c voltage is
applied through two fixed taps 180 deg apart and the output voltage is obtained from two
rotating brushes diametrically opposed to each other. If the winding is linear, varying
the position of the brushes varies the output voltage in accordance with a linear sawtooth
wave.
Many of these types have been provided with precious-metal contacts developed spe-
cifically to obtain low contact resistance with low contact pressure. Contact resistance
of a few hundredths of an ohm with contact pressures of about 50 to 80 grams has been
obtained, and a life of the order of a million operations has been realized. One type of
contact alloy widely used is Paliney No. 7, which consists of platinum, palladium, gold,
silver, copper, and zinc.
In another type of low-operating-temperature wire-wound potentiometer, known as a
multiturn potentiometer, the resistance wire is wound on an insulated metal mandrel
about 1/s in. in diameter which is then formed into a helix. The diameter and number of
turns of the helix vary, and potentiometers have been produced commercially with 2, 10,
15, 25, and 40 turns and with overall diameters of approximately 2, 3, 4, and 6 in. The
contact is arranged to follow the path of the helix. With this type very fine adjustments
are possible because of the comparatively long winding. By maintaining close tolerance
on the diameter of the mandrel and on the resistivity and diameter of the wire, linearity
of the order of ±0.1 per cent or better can be provided.
The straight winding type potentiometers heretofore described are not very suitable for
high-frequency applications. At frequencies above the audio range the straight winding
controls are affected by distributed capacitance and inductance. For higher-frequency
applications the characteristics of the individual control should be investigated.
POWER-TYPE RHEOSTATS. Toroidal Winding Type. This type is the most ex-
tensively used for applications from 25 to 1000 watts in the communications and electronics
fields. Adjustable resistors of this type generally consist of a toroidal ceramic form which
is wound with either round or ribbon-type wire over an arc of approximately 300 deg.
The wound form is then placed in a suitable ceramic base, and the entire unit, except for
the contacting surface of the wire, is given a coating of vitreous enamel under high tem-
perature. This form of construction permits a high wattage rating in a relatively small
volume of space.
Rheostats of this type are available in sizes ranging from approximately 1 Va in. to 12
in. in diameter and in rated wattage from 25 to 1000 watts. They are wound to resistance
values from a fraction of an ohm up to 10,000 ohms. The power rating of rheostats is
based on temperature rise in free still air. For those rated at 100 watts or less, the tempera-
ture rise is limited to 300 deg cent; for those rated above 100 watts the permissible tem-
perature rise is 350 deg cent.
These rheostats are available with either linear or tapered windings. Specific uses for
tapered rheostats are: (1) to provide a more uniform degree of control for all positions of
the contact, (2) to make possible the use of a smaller control, (3) to make it possible to
wind a higher resistance on a small control for specific applications, (4) to provide a par-
3-20
RESISTORS, INDUCTORS, CAPACITORS
§>
ticular controlled effect. An example of this last might be to provide a linear relationship
between control setting and motor speed in the case of motor speed controls, or to give
linear control of light output from a lamp. Figure 21 shows how the current varies (in
three typical rheostats) with per cent rotation of the contact.
For special applications, controls can be obtained with continuous 360-deg windings,
built-in toggle switches, or off positions at either end of the rotation.
Metal Type. Another power type of rheostat utilizes mostly metal in its construction.
The wire or ribbon is wound on a strip of aluminum with asbestos as insulation between
the wire and aluminum strip. The winding is formed into a circular shape and is assembled
in a die-cast aluminum base with mica sepa-
rating the winding from the base. Owing to
the close proximity of the winding to the
aluminum parts, the heat is carried away
from the winding more rapidly than in the
ceramic types. As a result, for the same
wattage dissipation the temperature rise is
somewhat lower.
Standardization requirements and per-
formance capabilities of power-type rheostats
for use in military applications are con-
tained in Joint Army-Navy Specification
JAN-R-22.
Tubular Slide-wire Type. The tubular
slide-wire type of rheostat is used extensively
for general laboratory applications, particu-
larly for precision measurements. They are
not generally used in commercial applica-
tions, inasmuch as they require considerably
more mounting space for equivalent wattage
ratings and are not as convenient as the
toroidal type.
V
(c
)
75
\
X
3 sectio
n taper
56.2
\
\v
\
•s.
(
B)
i
\
X
2 sect)
on taper
/•
•a
a
50
\
>,
/
25 —
( f.\
N
SX^
c
Unifon
(A). ..
n wmdinj
^"N.^
"--^
^^
1?
?•=>
"^•^^
6 25
0
(
8
) 20 40 60 80 1C
Per cent rotation of rheostat shaft
FIG. 21. Typical Curves of Current, Voltage, or
Wattage Relative to Shaft Rotation for Uni-
formly Wound and Taper-wound Rheostats
(Courtesy Ohmite Mfg. Co.)
STEP-TYPE POTENTIOMETERS, RESISTANCE BOXES, AND ATTENUATORS.
Potentiometers. This type consists of a rotary-type switch wired with fixed wire-wound
resistors between successive contact positions. A brush or blade rotated by a shaft makes
contact with contact studs or clips to which the fixed resistances are wired. The resistors
of each step may be all of equal resistance value or they may differ, depending upon the
nature of the application. The use of finite resistance steps permits a high degree of accu-
racy, especially in low- and medium-frequency applications. The accuracy at higher
frequencies is dependent upon the frequency characteristics of the individual resistors and
the type of switch structure. Likewise, the amount of power that can be dissipated is
governed by the fixed resistors and the type of switch used.
Decade Resistance Boxes. Many laboratory measurements and test instruments re-
quire the adjustment of resistance in a circuit in accurately known steps of pure resistance.
A decade resistance box consists of a number of individual resistance units equipped with
switching so that the total resistance is adjustable in decade units. Resistance units are
connected in series, and as many units can be connected as are required. To keep minimum
inductance and distributed capacitance, card-wound or spool-type resistor units are used.
Shielding and careful wiring arrangement also help keep capacitance low between resistor
units. Where residual inductance of the resistors must be considered, a switching arrange-
ment introduces a compensating winding as the resistance is adjusted to maintain constant
inductance.
Attenuators. Attenuators are used to insert known amounts of transmission loss in
circuits either for testing purposes or for volume level control. Step-type attenuators
basically consist of rotary-type switches and fixed resistors, as in step-type potentiometers.
They are arranged, however, to introduce various types of balanced or unbalanced resistive
networks into a circuit. They are designed electrically to be inserted between specific
input and output impedances, and only when so used will they insert the desired loss (see
Section 5).
CARBON COMPOSITION TYPE POTENTIOMETERS. Carbon composition poten-
tiometers are widely used in the communications and electronics fields on account of their
low cost, the higher resistance values in which they can be obtained, and their excellent
high-frequency characteristics. The types generally available are physically similar to the
small single-hole mounting, low-operating-temperature wire-wound controls previously
described. Two types of composition resistance elements are used, namely, the film-coated
type and the molded type. In the film-coated type, the carbon, filler, and binder mixture
SPECIAL-PUBPOSE RESISTORS
3-21
100
are applied as a film on a ring of insulating material. The film is specially processed so as
to minimize abrasion of the contact surface of the resistance element. In the molded type
the carbon composition is molded into a phenolic base. The contact is a carbon brush,
giving a carbon to carbon contact.
Linear and non-linear resistance rotation characteristics are obtainable in the composi-
tion types. The non-linear or tapered characteristic is produced by varying the proportion
of the conducting material to the insulating material in the mixture as the element pro-
gresses over its length. It is possible by blending in this manner to obtain a rather smooth
rate of change of resistance with angular rotation. Typical resistance-rotation character-
istics of composition-type potentiometers are
shown in Fig. 22. Curve A represents a clock-
wise linear characteristic except for a small
range at each end of the rotation. Curve B
illustrates a clockwise taper in which the first
50 per cent of the rotation introduces only 10
per cent of the resistance into the circuit,
Whereas the second half of the rotation inserts
the remaining 90 per cent of the resistance.
Curve C represents a clockwise taper in which
the first 50 per cent of the rotation introduces
90 per cent of the resistance and the second
half of the rotation inserts the remaining 10
per cent of the resistance. Curves D, E, and
F illustrate counterclockwise tapers of similar
characteristics to curves A, B, and C, respec-
tively.
Film-type composition potentiometers are
available in a variety of sizes ranging from
about 5/s to 1 1/2 in. in diameter and in watt-
age ratings from about 0.05 watt to 1 watt.
The available molded types are about 1 1/s in. in diameter and are rated at about 2 watts.
Resistance values obtainable range from about 50 ohms to 10 megohms.
For film and molded composition-type potentiometers, the voltage coefficient and the
effects of overloading, aging, temperature changes, and exposure to high humidity are
about of the same order as for film and molded fixed composition resistors. The molded
are inherently more stable in resistance than the film types. The tabulation below ob-
tained by tests compares typical film and molded types of 1-megohm resistance with
respect to their stability of resistance under varying atmospheric conditions. The tabu-
lation is in terms of average percentage change in resistance from that measured at room
conditions in successive tests on the same set of samples.
Per Cent Change in Resistance from Initial Resistance at 20° C under Varying Atmos-
pheric Conditions
90
| 70
leo
I 50
'3 40
c
S 30
$
^20
10
0
^^N
s
V
"^
^
f
-~*
"*"*"
^
\
V
\
/
\
/
^/
\
\
^ /
\/
^
r
-B
E-
^
/s
/\
y
\
\
/
v/
Cx
v/\
/
V
-D
/\
^
y
r\/
/
/
" \
/N
N
w
-F
1 /
/**.
-A
\
/
\
\
, \
/
/
-^
^
X-
*^^
"\
\
0 10 20 30 40 50 60 70 80 90 100
Per cent clockwise shaft rotation
FIG. 22. Nominal Resistance-rotation Char-
acteristics (Courtesy Ohmite Mfg. Co.)
After 96 Hr
After
After
After
After
at 40° C
After
4 Hr at
4Hrat
72 Hr at
72 Hr at
and 95%
72hr at
-18°C
-50°C
50° C
65° C
relative
90° C
humidity
Film type
4-3.0
+ 7.0
-7.0
-10.0
+ 14.0
-17.5
Molded type
+ 3.5
+ 5.5
-4.0
-5.5
+ 6.5
-5.5
Owing to their low inductance and capacitance, composition potentiometers are finding
wide use in high-frequency applications; an example is a common shaft tandem arrange-
ment of three rheostats, two of which are the series arms and the third the shunt arm of a
continuously adjustable T type attenuator for level control in television transmission over
telephone circuits at frequencies up to 4 megacycles.
7. SPECIAL-PURPOSE RESISTORS
In addition to the many resistors described so far, numerous special-purpose resistors
designed for particular applications should at least be mentioned here. In this category
are resistor standards such as those used in various measuring circuits and bridges which
are discussed in Electrical Measurements, Section 11 of this handbook. Thermistors and
varistors are used in an increasing number of applications in communications circuits, and
3-22 RESISTORS, INDUCTORS, CAPACITORS
they are fully described in the following articles. Resistors used primarily for heating as
in furnace elements and heavy-duty power controllers are covered in the Electric Power
volume of the Electrical Engineers' Handbook. A few other kinds are:
Resistance Lamps. In this type a special lamp filament having a high positive tempera-
ture coefficient serves either as a current-limiting, current-regulating, or protective device
in communication circuits. Those used to maintain constant current, as in the heater
circuits of vacuum tubes, are referred to as ballast lamps.
Dummy Antenna Loads. These may be in the form of (a) special space-wound resistance
elements enclosed in an evacuated glass bulb, (6) a wound mica card mounted between
metal castings to assist in carrying off the heat, or (c) a water-cooled film-type resistor in
which water is circulated through or over a ceramic core on which a resistor film has been
deposited.
RESISTORS IN PRINTED CIRCUITS. Printed circuit structures are a comparatively
recent development in which a network of resistors, in combination with capacitors and
inductors, is applied in the form of bands or ribbon to one or both sides of a supporting
structure, usually a thin ceramic plate. The necessary capacitors are also mounted on the
plate, and the plate itself may serve as the dielectric spacer and support for the capacitor.
Connections to both resistors and capacitors are made by lines of conducting paint. Thus
a complete coupling or filter circuit or even an entire amplifier circuit having several
stages of amplification may be assembled on a thin plate of 1 or 2 sq. in. of surface area.
The network is suitably terminated with wire leads, and the whole structure is given a
suitable protective covering. The resistors may be of metallic or carbon film or of the
composition film type. For composition and metal film type resistors produced by chem-
ical means, the material may be applied in the desired pattern by painting or silk-screen
process. For resistors applied by the metal-evaporation process, suitable stencils may be
used to limit deposition to the desired areas. Where a high dielectric body serves both as
the dielectric for the capacitors in the circuit and as the supporting panel for the resistors,
note that the increased distributed capacitance brought about in the resistor due to the
intimate contact with the high dielectric material may have a very marked effect on its
performance at high frequency. Printed circuits are finding increasing applications in
devices such as hearing aids, miniature radios, or wherever space is at a premium. Obvious
advantages are compactness and small size. Disadvantages are difficulties in manufacture
due to the necessity for processing all elements of the circuit at one time, which makes
close tolerance adjustment of individual elements impracticable and lessens the likelihood
of attaining the desired characteristics in all components. Also, in service, it is usually
necessary to replace the entire unit when a single element becomes defective.
BIBLIOGRAPHY
Industrial Control Standards, Publication 1C4-22, July, 1946, National Electrical Manufacturers Assoc.,
155 B. 44th St., New York, N. Y.
Blackburn, J. P., Components Handbook, Vol. 17, 1949, Radiation Laboratory Series, Massachusetts
Institute of Technology, Cambridge, Mass.
Curtiss, H. L., and Grover, F. W. Resistance Coils for A.C. Work, Bulletin Bureau of Standards, Vol. 8,
pp. 495-517 (1913).
B. Hague, Alternating Current Bridge Methods, 3d Edition, Chapters 2, 3, Pitman & Sons, 1932.
Bureau of Standards Circular 74.
Bureau of Standards Circular 100, 2d Edition, pp. 100-102.
Wireless Engineer, Vol. XII, No. 141 (June, 1935); No. 143 (August 1935).
High-Frequency Characteristics of Resistors, Report 520, Radiation Laboratory, Massachusetts Institute
of Technology, Cambridge, Mass.
Nettleton, L. A., and Dole, Fred E., Potentiometers, Review of Scientific Instruments, Vol. 17, No. 10,
pp. 356-363 (Oct. 19, 1946).
Brunetti and Curtis, Printed Circuit Techniques, Bureau of Standards Circular 468.
New Advances in Printed Circuits, Bureau of Standards, Miscellaneous Publication 192.
Data Sources:
Driver-Harris Co., Catalog R-46.
Wilbur B. Driver Co., Resistance Handbook.
C. O. Jelliff Mfr?. Co., Resistance Alloys.
Hoskins Mfg. Co., Catalog C.
VARISTORS AND THERMISTORS
By N. Y. Priessman
GENERAL. The term varistor, from the words variable and resistor, is applied to a
group of circuit elements broadly classified as non-ohmic resistances. The application
of the term varistor is restricted to devices in which the property of variable resistance
is provided by solid semiconductor materials. The semiconductors that have proved use-
COPPER-CUPROUS OXIDE VARISTOR
3-23
ful as stable circuit elements are those in which the current carriers are electrons as dis-
tinguished from those in which ions are transferred through the solid.
These non-ohmic resistors may be divided into two broad classes, depending upon
whether the resistance change is an electric field effect (varistors) or a temperature effect
(thermistors). The field-effect varistors may further be divided into rectifier varistors
and symmetrical varistors. Rectifiers, such as copper oxide, selenium, silicon, and ger-
manium, exhibit quite different values of resistance depending on the polarity of the
applied voltage. Symmetrical varistors such as Thyrite, Metrosil, Atmite, and silicon
carbide show no rectifying properties. Thermistors (see article 10) change resistance
markedly with changes of temperature but do not, independently of temperature change,
possess a non-linear resistance characteristic.
0.0025"-0.0040"
FIG. 1. Copper Oxide Varistor Cell
8. COPPER-CUPROUS OXIDE VARISTOR
The copper-cuprous oxide varistor consists essentially of a piece of sheet copper about
0.050 in. thick in the form of a disk, washer, or plate which has been oxidized so as to form
on its surface a layer of red cuprous oxide. A thin layer of conducting material is applied
to the exposed surface of this oxide to provide a contact, known as the outer contact. The
mother copper provides the other electrode. Figure 1 shows an enlarged and out-of-scale
cross-section of such a varistor cell.
The manufacturing techniques, although differing in detail with various manufacturers,
depending on the particular qualities in the product they are interested in, have in common
the following: the desired form of cell is blanked
from sheet copper (usually the grade known
as Chile copper), chemically cleaned, oxi-
dized in air atmosphere at a temperature in
the neighborhood of 1000 deg cent for some
10 to 20 minutes to form a layer of cuprous
oxide 0.003 to 0.004 in. thick, held for some
minutes at a temperature of about 550 deg
cent, and then quenched in water. At this stage the cuprous oxide (red) is covered with
a thin layer of cupric oxide (black) which must be removed by chemical action. The
means of providing an outer contact vary with the manufacturer. The following means
are in common use: (a) painted-on contacts of "aqua-dag" (colloidal graphite), (b) elec-
troplated contacts, and (c) contacts of gold or silver produced by the well-known tech-
niques of evaporation in vacuum.
The electrical properties of the varistor may be altered significantly by suitable varia-
tions in the fabricating processes, as for example by the addition of metallic impurities to
the copper (such as thallium) ; by changes in time, temperature, and atmosphere of the
heat treatments; or by changes in rate of cooling and quench temperature, etc.
The current-voltage characteristics of a varistor cell commonly used in communication
circuits is shown in Fig. 2 in the "Chile copper" curves. The "forward characteristic"
exhibited by the cell with the mother copper negative and the outer contact positive is
the flatter branch of the two curves. The "reverse characteristic" which obtains when the
copper is positive and the outer contact
negative is shown by the steeper branch.
Considering in detail the forward charac-
teristic curve the varistor behaves very
much like an ohmic resistor at voltages
below 0.05. As the voltage increases
above this the current increases rapidly;
that is, the resistance decreases. The seat
of this potential dependent resistance as
well as of the rectifying property is in the
interface between the cuprous oxide and
the copper. This interface is variously
called blocking layer, junction layer, bar-
rier layer, etc. As the voltage increases
above 0.5 volt the current increases less
FIG. 2. 1/2" Diameter Copper Oxide Varistor Cell
Representative Voltage-current Characteristics
rapidly and the resistance approaches a limiting constant series resistance, which is
mainly the body resistance of the oxide layer itself. The series resistance of the outer
contact is small compared with the body resistance of the cuprous oxide layer and is
non-rectifying. The thallium-copper cell behaves similarly but with reduced currents
in both directions.
3-24
RESISTORS, INDUCTORS, CAPACITORS
35
~30
S
I 25
§15
$*~
\
0.01 0.050.1 0.5 1. 5 10 50100 5001000
Time of application in seconds
FIG. 3. Delation of Safe Reverse Voltage to Time of
Application for Typical Copper Oxide Cells at Ambient
Temperatures below 100° F and for Applications
Spaced at Least 1 Minute Apart
practice. Moreover these characteristics change
resistance increases with time and temperature
The forward current at a voltage is
proportional to the area of the cell or,
more accurately, to the area of the
outer contact. The reverse current is
not simply related to the geometry of
the cell. The characteristics of cells
in series may be obtained by sliding
the characteristic curves parallel to
themselves along the voltage axis, and
the characteristics of cells in parallel
by sliding the curves along the current
axis. In practice large areas may be
obtained most economically by large-
area plates.
Large deviations from the typical
characteristic curves shown are inherent
in the commercially manufactured prod-
uct even when produced under the
best controlled conditions of present
with time and use. While the forward
t, the reverse resistance decreases with
101
10"
icr
10
i
10
E ,
o 10'
10"9 10~8 1Q-7 1Q-* 10~5 10~4 10~3 10~2 10"1
Current in amperes
FIG. 4. Representative D-c Characteristic of 3/16-in.-diam. Copper Oxide Varistor Cell (Chile Copper)
continued application of reverse voltage. In general this should not exceed 4 volts (see
Fig. 3) . These effects again vary from batch to batch.
Large negative temperature coefficients
of resistance both in the forward and
reverse direction are characteristic of these
devices. No simple law such as holds for
metallic conductors is applicable, and
the variation of resistance with tempera-
ture may best be displayed graphically as in
Fig. 4.
The effect of exposure to moisture is to
reduce the reverse resistance of all types
of cells. This is especially troublesome in
the small-diameter, very-high-reverse-re-
sistance cells. The forward resistance of
cells with aqua-dag contacts is increased
by exposure to moisture. It is customary
in the use of varistors as circuit elements
to provide substantial moisture-proofing
in the form of organic coatings, potting in
wax, etc.
Structures. The 3/4-in.-diameter and
larger cells are usually made in the form
of a washer and clamped together with
wiring terminals on an insulated bolt.
The 1/2-in.-diameter and smaller cells are
+Volts
FIG. 5. Voltage Limiter, Two l/2-in.-diam. Cop-
per Oxide Varistor Cells (Copper plus Thallium)
BIBLIOGRAPHY
3-25
FIG. 6. Bridge Connected Modulator
usually assembled with wiring terminals and pressure spring in cylindrical cavities in
insulating blocks.
Ratings. When copper oxide varistors are used as current-supply rectifiers their ratings
are based on four factors on which definite specifications should be made, with allowance
for aging. These factors are (1) the d-c voltage and current output, (2) the a-c voltage
input, (3) the ambient temperature, and (4) the means for cooling the varistor cells.
APPLICATIONS. Voltage Limiter. It may be seen from Fig. 2 that as the voltage in
the forward direction increases from 0.1 to 1.0 volt the current increases more than 1000
fold. A varistor may be connected across
the input terminals of a network to act as
a bypass when applied voltages are sub-
stantially above the normal level. Figure
5 shows the resistance- voltage characteristic
of such a varistor in which two V2-in.-diam-
eter cells of thallium copper (see Fig. 2) are
connected in parallel opposing so that the
combination has a symmetrical resistance-
voltage curve. The resistance is greater
than 10,000 ohms for voltages up to 0.1 volt
and drops to about 5.0 ohms at 1.0 volt. As the voltage increases above 1.0 volt the resist-
ance decreases but little; it is being limited by the body resistance of the copper oxide layer.
Modulator. Copper oxide varistors are extensively used both as modulators and de-
modulators in carrier telephone systems. A bridge-connected modulator is shown in
Fig. 6. The carrier voltage ec is made large compared with the signal voltage ev. When
the carrier voltage is of such polarity as to bias the varistors in the forward direction they
will all be low in resistance, offering substantially a short circuit to the signal current.
When the carrier voltage reverses the varistors all have a high reverse resistance and the
signal current appears in R%. It is desirable to prevent unmodulated carrier current from
appearing in R%, and this is done by selecting the four varistors in the arms of the bridge
to have voltage-current characteristics very closely alike
so that the bridge is balanced throughout the cycle of carrier
voltage. (A complete discussion of the varistor modulator
is given by Caruthers, Bell System Technical Journal, Vol.
18, 315 [1939].)
Control of Telephone Relays. Various configurations of
relay windings and varistors may be used to modify the
response characteristics of relays. Several such arrange-
ments are shown in Fig. 7: (a) delayed release with prac-
tically no effect on operate time; (6) delayed operate with
practically no effect on release time. Steady operation of
relays from an a-c source is obviously possible using the
varistor as a rectifier. In the simple arrangement shown in
Fig. 7(c), the reverse half-cycle is bypassed through the
varistor which also affords a path for the slow decay of
current established in the winding during the previous posi-
tive half-cycle.
Varistors are used in a circuit network known as a
"compandor" — a contraction of the words "compressor"
and "expandor." A compressor is a non-linear transmission
network in which the range of signal power output is com-
pressed relative to the range of power input. An expandor is a network which provides
the inverse action. Detailed discussion of such circuits, also called "vario-lossers," may
be found in Bennett and Doba, Trans. A.I.E.E., Vol. 60, 17 (1941).
(a)
BIBLIOGRAPHY
A Bibliography on Metallic Rectifiers and Their Principal Applications, published by the American
Institute of Electrical Engineering, New York, N. Y. A bibliography of more than 500 items on
fundamental theory, various types of rectifiers and their applications.
Bibliography of Literature on Rectifiers and Semi-conductors, Royal Aircraft Establishment, Issue 4,
August 1946.
H. C. Torrey and C. A. Whitman, Crystal Rectifiers, Rad. Lab. Series, McGraw-Hill Book Co,
3-26
RESISTORS, INDUCTORS, CAPACITORS
9. SILICON CARBIDE VARISTORS
It has long been known that silicon carbide will, under suitable conditions of contact,
exhibit a non-linear relationship between current and voltage. This may readily be
demonstrated by measuring the voltage-current characteristic of a mass of small particles
of silicon carbide compressed between metallic electrodes. As the voltage is increased
from zero the current increases, at low voltage in direct proportion to the voltage and then
much more rapidly. If the number of particles in the mass is large and the distance be-
tween electrodes large compared with the dimensions of the particles the non-linear resist-
ance of the device is independent of polarity.
Experiments upon single particles with suitably made contacts indicate that the body
resistance of the particle is small, ohmic, and independent of polarity.
The non-linear conduction exhibited by the mass of particles results from the voltage-
dependent resistances at the point-to-point contacts between the granules of silicon carbide.
The overall resistance characteristic may be thought of as due to large numbers of non-
linear resistance contacts arranged at random in series and parallel. In a statistical sense
the aggregate displays no dependence upon the direction of current flow. This varistor
is an example of a "symmetrical non-linear resistor."
The simple device of containing a mass of silicon carbide particles under pressure be-
tween electrodes does not have the stability of characteristic under use conditions to afford
wholly reliable circuit elements.
In 1930, McEachron (see Journal A.I.E.E., Vol. 49, 410 [1930]) described a silicon
carbide ceramic non-linear resistor to which the name Thyrite was given. The material
consists of silicon carbide particles bonded in a ceramic matrix. Similar materials are
known under various names such as Metrosil and Atmite.
The essential steps of manufacture are these: suitable silicon carbide particles, clay and
water, sometimes with a minor constituent such as carbon, are mixed to form a plastic
mass. The mass is partially dried and forced through screens to obtain a slightly damp
granular powder. This material is compressed under high pressure into desired shapes,
generally flat disks or rods. These pieces are further dried and heat treated in a reducing
atmosphere at a temperature in the neighborhood of 1200 deg cent. The fired pieces are
hard and strong and have mechanical properties quite similar to those of dry process
porcelain. Electrodes on the opposite plane faces are provided by spraying or Schooping
a layer of metal such as brass, copper, aluminum, or tin. The piece is then usually im-
pregnated with a moisture-repellent organic substance to prevent pickup of water, which
adversely affects their electrical stability.
The electrical properties of the product are profoundly affected by the parameters of
process: materials, particle size, moisture content, forming pressure, and especially tem-
perature, time, and atmosphere of the heat treatments. The products of different manu-
facturers differ somewhat in electrical
properties, most importantly in the de-
gree of non-linearity, and the character-
istics of Fig. 8 are to be taken only as
generally indicative. The current-volt-
age characteristic shown is closely rep-
resented by the equation
1000,
Co'ntinuou's
operation '
intermittent
operation
10'3 ICT
Amperes
10"
FIG. 8. Representative D-c Characteristics of Some
3/4-in.-diam. Silicon Carbide Varistor Disks
where I = current through the piece,
E = voltage applied to the piece, Ci and
Cz are constants depending on the mate-
rial and geometry of the piece, and n is
an exponent the value of which depends
on various factors in the manufacturing
process and generally lies between 3.5
and 5.0. Some manufacturers indicate
values of n as high as 7.0 but only for
pieces having resistances much above
the range indicated in Fig. 8.
The variation of characteristic through control of manufacturing processes and geometry
of the piece permits coverage of an enormous range of current and voltage. This range
may be further extended by connection of pieces in series or parallel. It is to be noted
from Fig. 8 that as the resistance of the piece decreases the value of n decreases also, 'and
this being typical of aU manufacturers7 products may be considered an inherent charac-
SILICON CARBIDE VARISTOKS
3-27
teristic of the presently made material. In consequence it is not possible with this device
to obtain marked non-linearity at low voltage.
In common with semiconductors the silicon carbide varistor exhibits a negative tem-
perature coefficient of resistance. The coefficient does not have a single value but varies
both with the material and with voltage and temperature. The values of the coefficient
at constant voltage cover a spread of from 0.3 per cent to 0.9 per cent per degree centigrade
in the normally used range of temperature. The higher values of temperature coefficient
are observed at the lower voltages.
At high frequencies consideration should be given to the presence of a capacitance
effectively in parallel with the non-ohmic resistance. The exact value of this capacitance
is determinable only by measurement, but the order of magnitude may be calculated by
assuming the material to have a dielectric constant of 30 to 200.
Commonly used shapes are rods and disks. Small disks and rods may be furnished with
leads soldered to the metallic electrodes on the faces of the piece. Disks are also made
with holes in the center and clamped together with wiring terminals by means of a central
bolt. Disks and rods of all sizes are used with spring clip mountings which furnish mechan-
ical support and electrical connections.
"When used under high humidity conditions, or at low currents, the organic impregnant,
referred to in the description of the fabricating process, may not be sufficient protection
against moisture and further precautions may be necessary.
Approximate values of mechanical and thermal properties of importance in circuit
element design are as follows:
Bulk density 2.35 grams per cu cm
Compression strength 15,000 to 23,000 Ib per sq in
Specific heat 0.17 to 0.21 cal per gram per deg cent
Thermal conductivity 0.0034 cal per cm per sec per deg cent
Requirements on the current-voltage characteristic for a particular application may be
stated in a number of ways; the following are commonly used.
(a) The voltage J$\ at a current Ji shall be greater than some value, and the voltage E%
at a current /a, where /2 is greater than Ji, shall be less than some value. This statement
of requirements contains implicitly a requirement as to the minimum value of n.
(6) The voltage at a given current I shall be equal to a value E ± X per cent, and the
value of n shall lie within certain limits throughout a range of current.
It is to be noted that considerable differences in characteristic may exist between pieces
meeting a set of such requirements. In commercial manufacture the range of voltage at a
given current commonly runs ±20% about the average. Accuracy of meters used in
checking requirements is im-
portant since errors in volt-
age readings are to be multi-
plied by n in determining
their effect on current read-
ings.
Self-heating resulting from
power dissipation in the var-
istor lowers its resistance
(negative temperature coef-
ficient of resistance) , but this
effect is in general reversible;
that is, no permanent effects
on the characteristic are pro-
duced by moderate heating,
say from 100 to 150 deg cent.
The safe upper limit of heat-
ing is oftentimes determined
by the moisture-resistant or-
ganic compound used as an
impregnant. As shown in
Fig. 8, 1.0 watt for a disk of
3/4-in. diameter suspended in
free air at 50 deg cent is a limit recommended by one manufacturer. Very heavy transient
currents may alter permanently the characteristic, usually in the direction of decreasing
the resistance.
APPLICATIONS. (1) A silicon carbide varistor connected across the terminals of an
electromagnetic winding acts to limit the surge voltage generated when the field is opened,
Surge voltage prote
by use of silicon ca
vanster
0.05 0.1
5 10
30 50 100
0.5 1,
Milliamperes
FIG. 9. Surge Voltage Protection by Use of Silicon Carbide Varistor
3-28 RESISTORS, INDUCTORS^ CAPACITORS
As shown in Fig. 9 the maximum value of voltage across the varistor may be determined
from the point on the voltage-current characteristic corresponding to the steady-state
value of current IQ in the winding. As compared with an ordinary resistance shunt across
the winding to secure the same voltage-limiting effect, the varistor dissipates much less
power when the coil is steadily energized,
(2) In certain carrier telephone system filters exposed to high incoming voltage, the
condenser of a bigh-Q combination of coil and condenser has been protected by a varistor
in shunt.
(3) Some of the smaller telephone switchboards have line lamps connected directly in
the subscriber's loop for signaling. These line lamps are exposed to electrical disturbances
that may be impressed on the outside lines, and if the disturbances are severe enough the
lamps may be burned out. Silicon carbide varistors have been used very effectively in
parallel with the lamp to bypass large incoming surges. The high resistance of the varistor
at the normal signaling level has no appreciable effect on the lamp illumination.
(4) Use is made of varistors to protect contacts controlling inductive circuits from the
deleterious effect of sparks resulting from the opening of such circuits. Usually the varistor
is connected across the winding rather than across the contact to avoid continuous current
drain. Though such an arrangement is useful it is not a satisfactory general solution of the
problem. The varistor increases the release time of the relay or switch magnet, though
not to the extent that an ohmic resistance of equivalent spark quenching action would do,
and it does not entirely eliminate high-frequency oscillations across the opening contact
due to the associated wiring.
BIBLIOGRAPHY
McEachron, J. A.I.E,E., Vol. 49, 410 (1930). (Thyrite.)
Fairweather, J. A.I.E.E., Pt. I, Vol. 89, 499 (1942). (General. Contains bibliography of 59 items.)
Ash worth, Needham, and Sillars, J. A.I.E.E., Pt. I, Vol. 93, 385 (1946). (General. Contains bibli-
ography of 25 items.)
Brownlee, Gen. Elec. Rev.. Vol. 37, 175 (1934); Vol. 37, 218 (1934). (Calculation of circuits.)
Grisdale, Bell Labs. Record, Vol. 19, 153 (1941). (General.)
Vigren, Telegrafstyrelsen, No. 7, Vol. 9, 138 (1942). (Contact protection.)
Royal Aircraft Establishment Issue 4, August 1946, Bibliography of Literature on Rectifiers and Semi-
conductors.
10. THERMISTORS
Thermistors or thermally sensitive resistances are devices made of solid semiconductors
the electrical resistance of which varies markedly with temperature. This phenomenon
has long been known, Faraday having observed that the resistance of silver sulfide de-
creased rapidly as the temperature increased. Since that time it has been determined that
a great number of materials classed electrically as semiconductors exhibit high negative
temperature coefficients of resistance. Semiconductors have specific resistances at room
temperature much greater than those of metallic conductors and much less than those of
insulators. This very wide intermediate range of resistivities is not bounded precisely
but may extend from 0.1 ohm cm to 109 ohm cm. Materials commercially employed in
thermistor circuit elements have a much narrower range of resistivity, roughly from
10 ohm cms to 100,000 ohm cm.
The materials of thermistor construction include a wide variety of metallic oxides. In
common use are the oxides of uranium and various mixtures of the oxides of magnesium,
manganese, titanium, iron, nickel, cobalt, zinc, etc. The common method of fabricating
is to heat the oxides in the form of compressed powders to a temperature at which they will
sinter. At the sintering temperature the powders recrystallize to form a dense, hard,
ceramic-like solid of homogeneous composition. The sintered-powder process permits the
mixing of various oxides in suitable proportions to produce a wide range of electrical and
thermal characteristics and permits as well the fabrication of a great variety of shapes and
sizes of the completed piece.
Forms. Three forms of thermistors are common — disks, rods, and beads. A thin plate
or flake form has also been described and is hi limited use (see Becker et al., Bell Sys. Tech.
Jour., January 1947). Disks range in diameter from 0.125 to 2.0 in. and in thickness from
0.030 to 0.250 in. Rods are made in diameter from 0.030 to 0.250 in. and in length from
0.050 to 2.5 in. Bead diameters range from 0.006 to 0.060 in.
Properties. The relations between specific resistance and temperature of several
thermistor materials are shown in Fig. 10 and for comparison the resistance-temperature
relation of platinum. In Fig. 11 the log of the specific resistance is plotted against the
reciprocal of the absolute temperature. It is seen that the curves are very nearly straight
lines, and so to a close approximation
THERMISTOES
3-29
log p
const. + j8 • — or
const.
from which.
where T = temperature in degrees Kelvin, p — po when T — To, 0 is numerically propor-
tional to the slope and is of the dimensions degrees Kelvin. From the definition of tem-
perature coefficient a. = (l/R)(dR/dT} it is 7
seen that c
10s
10'
E
o
I 10*
c
8 10°
Crt
2 10 '
10"
10"
•S
*io*
Iff
io~lLH
100 0 100 200 300 400
Temperature in degrees centigrade
FIG. 10
1.0
2.0
3.0 4,0
1
Temperature in degrees Kelvin
FIG. 11
THERMISTOR APPLICATIONS. Direct utilization of the resistance-temperature
relation is a broad field of use including resistance thermometry, compensation for the
positive temperature coefficient of other resistive circuit elements, temperature control,
and the like. In all these applications the self-heating effect of any current in the thermis-
tor is kept small so that the resistance is fully controlled by the ambient temperature.
The equation previously given for the relation between resistance and temperature may
for purposes of general calculation be
Table 9. Temperature-resistance Characteris-
tic of a Typical Thermistor Thermometer
considered independent of temperature.
Table 9 shows temperature-resistance
characteristics of a typical thermistor
thermometer. With an ordinary Wheat-
stone bridge and galvanometer and a
suitably calibrated thermistor thermom-
eter a precision of 0.001 cent deg is
readily obtainable.
The use of thermistors in conjunction
with relays, valves, etc., for temperature
control is closely akin to their use in
thermometry. The larger currents re-
quired for relay operation necessitate
design consideration of the self-heating
effects in the thermistor.
Thermistors are used to compensate
for changes in resistance of electrical
circuits caused by ambient temperature
variations. Shunting the thermistor by
a parallel resistance sometimes improves
the accuracy of the compensation. Consideration should be given to like temperature
exposure of the thermistor and the compensated circuit element, and also to the effects
on both of power dissipation.
Small thermistors have been used extensively to measure power in very high-frequency
test sets. Suitably mounted in a properly terminated waveguide a thermistor bead absorbs
effectively the entering power, and the consequent heating of the bead produces a change
Temperature,
deg cent
Resistance,
ohms
Temperature Coefficients
B,
deg cent
a, per cent
per deg cent
-25
0
25
50
75
100
150
200
580,000
145,000
46,000
16,400
6,700
3,200
830
305
3,780
3,850
3,920
3,980
4,050
4,120
4,260
4,410
-6. 1
-5.2
-4.4
-3.8
-3.3
-3.0
-2.4
-2.0
Dissipation constant in still air, approximately 4
milliwatts per degree centigrade; thermal time constant
in still air, approximately 70 sec; dimensions of thermis-
tor, diameter approximately 0.11 in., length approxi-
mately 0.54 in.
3-30
RESISTORS^ INDUCTORS, CAPACITORS
100
in resistance which may readily be measured with high accuracy. Calibrating may be
done with d-c or low-frequency power.
The self-heating effect of current through a thermistor, primarily the bead type, results
in interesting and useful non-linear
relationships between current and
voltage. Figure 12 shows a "steady-
state" characteristic of a particular
form of bead thermistor. At small
currents the power dissipated is too
small to heat the thermistor appre-
ciably, and the resistance remains
constant. With increasing current the
°a effects of self-heating become evident;
\ the temperature of the thermistor rises
and the resistance decreases. As the
current continues to increase, the slope
of the curve changes from positive to
negative and in this latter region the
thermistor exhibits a negative value of
dv/dl, that is, a negative resistance.
The numbers along the curve give the
rise in temperature in degrees centi-
! grade above the ambient. The change
in resistance of the thermistor does not occur instantaneously with current change because
of its thermal mass.
The heating and consequent reduction of resistance by the continued passage of current
is used to obtain delayed response circuits as well as non-response to short-duration surges
by connection of the thermistor in series with a
relay.
Figure 13 shows a combination of thermistor
and resistances to obtain either a speech volume
limiter or a volume compressor. The speed of
response of the thermistor is adjusted to syllabic
frequency or slower to eliminate the wave-form
distortion and peak chopping common to quick-
acting non-linear devices.
100
.LLm i tejLO c_co m p r ess o
Load
Directly heated
" thermistor
FIG. 14
4 8 12 16
Current in miliiamperes
FIG. 13
20
Curve 1, thermistor characteristic
Curves 2 and 4, ohmic resistor char-
acteristics
Curves 3 and 5, combined charac-
teristics
Figure 14 shows a thermistor in the negative
feedback circuit of an amplifier to obtain con-
stant level output independent of variations of
signal input. This use is of great importance in
telephone carrier systems to correct for variations
in overall line loss. The simple bead structure
previously described is not adequate for this pur-
pose since its resistance and hence the amount of
feedback would be subject to change with changes
in ambient temperature. Temperature compen-
sation is economically obtained by associating a heater winding with the bead and regulat-
ing the input current to the heater to produce a constant temperature surrounding the bead.
BIBLIOGRAPHY
1. Pearson, G. L-, Thermistors: Their Characteristics and Uses, Bell. Labs. Rec., November 1940,
. 85.
. ., ,
p. 85.
2. SiUars, R. W Materials and Devices of Falling Resistance-Temperature Characteristics, J. Sci.
InsL, Vol. 19, No. 6, 81 (June 1942).
££' T- r8^ ^ V*n Iima' Ml' Thermistors, Their Characteristics, Uses and Associated Circuits,
Office of Publication Board Report PB-3407, 1945, Dept. of Commerce, Washington 25 D C
PKOPERTIES OF AIR-CORE INDUCTORS 3-31
4. Gray, T. S., and Van Dilla, M., A Thermistor Electronic Thermoregulator, Office of Publication
Board Report BP-3402 1945, Dept. of Commerce, Washington 25, D. C.
5. Gaffney, F. J., Microwave Measurements and Test Equipments, Proc. I.R.E., Vol. 34, 775-793
(October 1946).
6. Becker, J. A., Green, C. BM and Pearson, G. L., Properties and Uses of Thermistors — Thermally
Sensitive Resistors, Electrical Engineering, Vol. 65, November 1946, and Bell Sys. Tech. J., Vol.
26, No. 1, 170-212 (January 1947).
7. Pearson, G. L., The Physics of Electronic Semi-conductors, Trans. A.I.E.E., Vol. 66, 209 (1947).
8. Roloff, C. C., Thermo-variable Resistors, Elec. Rev. Lpnd., Vol. 140, 315 (February 1947).
9. Verwey, Haayman, and Romeyn, Semi-conductors with Large Negative Temperature Coefficient
of Resistance, Phillips Tech. Rev., Vol. 9, No. 8, 239 (1947).
10. Montgomery, C. G., Technique of Microwave Measurements, M.I.T. Rad. Lab. Series. (Use of
thermistors, Chapter 3.)
11. Deeter, E. L., Null Temperature Bridge, Electronics, Vol. 21, No. 5, 180 (May 1948).
INDUCTORS WITH AIR CORES
By L. M. Hershey
Of the many different types of air-core inductors in communications equipment today,
the solenoid and the universal winding are most widely used. Torroidal windings, and
other types such as the bank winding, spiral winding, and basket weave, are sometimes
found.
The single-layer solenoid is used in untuned or tuned circuits, for resonant circuits,
chokes, and in various other applications where a high Q, low distributed capacitance,
mechanical strength, or ease of construction is of importance. More space is required to
accommodate a single-layer solenoid than a universal winding of any type, for a given
inductance; at frequencies below about 1 or 2 me, space considerations frequently prevent
the use of the single-layer solenoid.
The universal winding is popular in applications similar to those listed above for the
single-layer solenoid but generally at frequencies below about 2 me. It produces a coil
having fairly high Q with low distributed capacitance, and mechanical strength. The
distributed capacitance of a universal winding can be decreased by winding it on a narrower
cam or by building it in a number of sections, each of which is a universal winding, with
these sections connected in series. This multisection universal winding also can be ad-
justed to close inductance tolerance requirements by moving one of the end sections (some-
times called a "pi") nearer to, or away from, the adjacent section.
Many special types of windings are in use as tuned loops in the broadcast band (540 to
1600 kc). Among these types are the multilayer solenoid, basket weave, single-layer
solenoid, and spiral winding.
Air-core inductors are used at frequencies up to about 200 me, or up to a frequency
where a transmission line becomes more convenient. The transition region between coils
and transmission lines appears to be extremely broad.
The choice of the type of inductor is generally dictated by such practical considerations
as available space or cost as well as by circuit considerations. Untuned primary coils
and chokes of less than about 10 to 20 ^h are usually solenoid windings. When greater
inductance is required, the universal winding is used.
11. PROPERTIES OF AIR-CORE INDUCTORS
FIGURE OF MERIT. The figure of merit of an inductor is the ratio of its effective
reactance to its effective resistance. This factor is called the Q of the inductor.
POWER FACTOR. The reciprocal of the Q of the inductor is equal to the power factor
of the circuit within very close limits for values of Q above about 20. The power factor
is more convenient than the Q to use in the calculation of certain circuit phenomena. For
instance, the power factor of a circuit formed by an inductor shunted by a capacitor is
the sum of the power factors of the two branches of the circuit, while the Q of the circuit
is the reciprocal of the sum of the reciprocals of the Q's of each branch.
Like resistance and conductance, both the power factor and the Q are useful concepts,
and the choice depends upon their application to the particular problem.
TIME CONSTANT. The time constant of an inductor in series with a resistor (the
resistor may represent the internal resistance of the inductor) is L/R; it is the time in
seconds required for the current, through an inductor of L henries in series with a resistor
of R ohms, to reach 0.632 of its final value if a voltage is applied suddenly, or for the current
through the series circuit to fall to 0.368 of its initial value if the inductor and resistor are
short-circuited suddenly.
3-32 RESISTORS, INDUCTORS, CAPACITORS
COIL LOSSES. The principal losses in an air-core inductor are those due to PR loss
in the conductor and the dielectric losses in the coil form, wire insulation, impregnating
material, etc. Eddy-current losses also occur in the conductor. At very high frequencies
the losses due to radiated power may be appreciable. Additional losses occur outside the
coil itself whenever any magnetic, dielectric, or conducting material is within the field of
the coil.
The attainment of a maximum Q in a given space is one of the most common problems.
At the lowest frequencies, the problem is to obtain the lowest d-c resistance for a given
inductance. As the frequency becomes higher, skin effect (the tendency of an alternating
current to flow along the outside surface of a conductor) becomes apparent, and is measur-
able even at power-line frequencies. Dielectric losses also begin to be noticeable at very
low frequencies. Throughout the radio-frequency spectrum these two causes of power loss
are of extreme importance. For example, a well-designed coil operating at 1 me might
have a d-c resistance of less than 5 ohms and an apparent resistance greater than 10 ohms.
Coil losses may be minimized, and high values of Q realized, by careful choice of the type
of wire (to increase the surface area of the conductor through which the r-f currents flow) ,
by obtaining the optimum spacing between conductors, and by choosing the proper shape
of the winding for the available space.
It is sometimes desirable to design a coil with a certain value of Q so that, for instance, a
required band width can be produced without the use of an external damping resistance.
Then the designer may reverse his usual thought processes and use a "poor" shape factor
for his coil, a conductor either larger or smaller than the optimum value for maximum Q,
or use a value other than optimum for the spacing between conductors. Frequently, the
diameter of the coil form can be reduced until a desired low value of Q is realized.
DISTRIBUTED CAPACITANCE. Each turn of an inductor is coupled magnetically
to other turns of the same inductor. A certain small amount of capacitance between the
turns of a winding is unavoidably produced by their proximity. The effect of all these
small series capacitances across the whole inductor at its working frequency is called the
"distributed capacitance of the coil. The values of the distributed capacitances of various
common types of air-core inductors range from a small fraction of a micro-microfarad up
to 10 or more ju/if. In general, a coil having a large ratio of length to diameter has a low
distributed capacitance, and it is obvious that finer wire and greater spacing between turns
will result in lower distributed capacitance.
Dielectric losses generally are decreased by a reduction in distributed capacitance.
However, the changes necessary to reduce the dielectric losses and distributed capacitance
(reducing the wire size, increasing the spacing between turns) finally begin to increase the
copper losses in the conductor faster than the dielectric losses are decreased. An optimum
design is a compromise between all these factors, and in a resonant circuit the distributed
capacitance is frequently of lesser importance than the Q of the inductor; therefore, the
capacitance is disregarded, while efforts are directed toward the attainment of minimum
total losses. In r-f choke coil design, a minimum value of distributed capacitance is usually
desired, while a Q higher than 5 or 10 produces a negligible effect. Therefore, choke coils
are frequently wound with a minunum wire size, on long slender forms, and with relatively
large spacing between turns.
12. ELECTRICAL DESIGN CONSIDERATIONS
TYPES OF CONDUCTORS. Copper wire is most commonly used in inductors. Copper
tubing, or strips, are sometimes resorted to at frequencies above about 50 me, Litz wire,
composed of a number of strands of fine enameled wire (from about No. 38 to No. 44),
produces lower r-f resistance than a single wire of the same area of cross-section. It is
most effective in the lower-frequency part of the radio spectrum, below about 2 me.
Above this frequency the r-f currents appear to flow along the outside of the group of
conductors and the effectiveness of litz wire is not so apparent.
Bare copper wire is rarely used for inductors. Tinned wire is found occasionally on
space-wound solenoids; silver plating is also used occasionally on the heavier conductors
normal for this type of coil. Silver plating offers the advantages of high conductivity on
the surface of the conductor where higher-frequency currents flow, soldering to the con-
ductor is made easy, and an attractive and fairly durable finish is produced.
TYPES OF WIRE INSULATION. Silk and cotton have been the most common mate-
rials for wire insulation on air-core inductors. Coil wire is made with a spiral wrapping,
adding about 0.002 in. to the diameter of the wire for silk or about 0.004 in. for cotton.
This ia called a "serving" of silk or cotton. A double serving may be used, with the second
serving spiraling in a direction opposite to that of the first serving. This is known as double-
ELECTRICAL DESIGN CONSIDERATIONS 3-33
silk or double-cotton insulation; it is usually designated D.S. or D.C. For instance, a
No. 38 bare wire with, double silk insulation could be described as 38 D.S. Celanese and
nylon are rapidly replacing silk and cotton as insulation for coil wire. Braided fabric
insulation is also used to some extent.
An enamel coating is used, either alone on wire for solenoids, or with one or more servings
of silk or one of the other serving materials over it. The enamel adds about 0.001 in. to
the wire diameter. Plastic coatings can be added to conductors, and almost any required
outside diameter can be produced in this manner.
Litz wire, as it is made in this country, consists of three or more strands of enameled wire
with one or more servings of silk, cotton, celanese, or nylon, around the group of wires.
The strands are either twisted in a regular fashion as they are wrapped or simply placed
side by side parallel to each other. The twisted method produces a slightly higher Q under
some conditions.
BEST COIL SHAPE. Formulas are available which express the best shape factor and
winding pitch of a single-layer solenoid under idealized conditions. In a practical design
problem these formulas serve as a valuable guide.
It has been shown that with a given length of wire, wound with a given pitch, the single-
layer coil which has the maximum inductance value is so shaped that the ratio
Diameter -f- Width of winding = 2.46, approximately.
Brooks has determined that there is a most efficient multilayer coil form to produce
the maximum inductance with a given length of conductor. This most efficient inductor
was produced as a compact multilayer cylindrical coil with a mean diameter 2.95 times
the side of the square cross-section. Other proportions varying somewhat from the op-
timum affect the inductance only slightly. It has been determined that, when the ratio
of mean diameter to side of square cross-section is 2.80, the resulting inductance is only
0.04 per cent less than the maximum value. It is generally convenient and within limits
of accuracy to consider the optimum form as having the dimensions: diameter equal to
3 times width, and width equal height of winding.
Precision design can be effected only when the inductor is solely for low frequencies.
The problem then of constructing an inductor of definite inductance for radio frequencies
resolves mainly into the problem of minimizing the resistance and distributed capacitance.
A coil is designed for a certain range of frequencies, and generally an attempt is made to
construct a coil with a uniformly high value of Q in this range. In consideration of these
and other requirements, a coil design will generally depart from the optimum proportions
indicated above.
It will be found that a practical coil is, in general, somewhat elongated in the direction
in which distributed capacitance will be minimized. For instance, a practical solenoid
is usually longer in proportion than is indicated by the formula above; a diameter-to-
length ratio of slightly over unity is common. The universal winding is frequently elon-
gated in the radial direction. A diameter-to-length ratio of about 0.7 was found to produce
the maximum Q over the broadcast band for a progressive universal winding on a 0.5-in.-
diameter Bakelite form.
Dielectric and eddy-current losses, which usually are neglected in the computation of
"best" coil shapes, appear to be primarily responsible for the noticeable discrepancies
between calculated and measured data.
SOLENOID WINDINGS. Single-layer solenoids are sometimes wound with each turn
touching the preceding turn; this results in fairly high values of distributed capacitance
and eddy-current and dielectric losses. The length of the winding, and consequently its
inductance, vary considerably from coil to coil in this type of winding because of variations
in wire size (unless the wire is selected to closer than the usual limits for its gauge) and
because of the failure of each turn to lie snugly against the next throughout its length.
Therefore, when the inductance tolerance of a coil is closer than a few per cent, it is cus-
tomary to "spin" a few turns — about 5 to 10 per cent of the total on the end of the coil.
These turns are wound with the same spacing as the main portion of the winding, but the
group of wires in the spun portion is spaced about 1/8 i*1- away from the balance of the coil.
These "spun" turns can be moved on the coil form nearer to, or away from, the balance
of the winding.
It is possible to wind a solenoid to very accurate length and inductance limits (on a form
of accurate diameter) on a winding machine or lathe adjusted to produce the desired
pitch per turn. This method allows uninsulated wire to be wound in a solenoid, if care is
taken to secure the turns properly on the form to prevent slippage after the coil is wound.
Depending upon the design requirements, the pitch may be chosen to give the minimum
spacing necessary to assure mechanical and electrical uniformity with maximum variations
in wire and insulation dimensions, or the spacing may be chosen for optimum electrical
performance.
3-34 RESISTORS, INDUCTORS, CAPACITORS
Solenoids are sometimes wound in a screw-thread groove in the coil form, but unless a
molded form is used it is difficult to maintain an accurate effective diameter of the groove
and inductance variations result. Also, winding the conductor in a groove may reduce
somewhat the Q of a very efficient inductor because of increased dielectric losses in the
material in the immediate vicinity of the conductor. A slight increase in distributed
capacitance will also result.
A simple manner in which to wind a single-layer solenoid is to choose insulation of the
proper thickness to space the turns properly when the insulated wire is close wound.
THE UNIVERSAL WINDING. This type of inductor is wound in single or multiple
sections ranging in widths from about 1/16 to 1/2 in. On a simple type of winding machine,
the width of the coil is controlled by a cam which oscillates the wire guide back and forth
in a linear fashion on the periphery of the form or on the next lower layer of the same
winding. The cam is geared to the main shaft of the winding machine. The main shaft
holds the coil form and rotates the coil as it is wound. The number of teeth in the gear
on the main shaft (or driven by the main shaft through a 1/1 gear ratio) over the number
of teeth in the gear on the camshaft is called the gear ratio. The wire is wound on the
form at an angle to the side of the coil form (winding angle) determined by the width of
the cam, the diameter of the coil, and the gear ratio. Simon has stated that a practical
limit of this winding angle is about 12 deg maximum. Above this value, the wire may
slip on the coil form and a poor winding will result. The winding angle becomes smaller
as the coil builds up, being approximately inversely proportional to the diameter of the
winding at any point; when this angle is reduced to about 6 deg the turns cross each
other at an angle which is too small and tend to align themselves in the spaces between
adjacent turns on the previous layer. The coil will not build up properly after this point
is reached.
When a coil must be wound up to an outside diameter about equal to, or greater than,
twice its inside diameter, it is frequently necessary to tolerate some slippage of the wire
on the form at the start of the winding. The winding problem is, of course, greatly facil-
itated when the designer restricts the height of the winding to a point within practical limits.
The winding angle is proportional to the cam width and also to the gear ratio, since the
gears drive the cam at a rate depending upon their relative number of teeth.
If gf, the pattern gear ratio, is the fraction q'/s', where both qr and s' are small whole
numbers, a simple and practical winding pattern should result. The number of cam
cycles per winding cycles is q', and the number of planes cutting the periphery of the
winding where interlaced crossing of turns occur is (s' — 1) .
In order to have the winding pattern repeat on consecutive winding cycles with the
required spacing between adjacent turns, the pattern gear ratio may be corrected by the
amount ±g'xw/2cqf, where x is the desired number of wire diameters between turns
(usually about 1.25), and w is the diameter of the wire. The plus sign produces a retro-
gressive winding; the minus sign produces a progressive winding. The gear ratio, g, may
be computed g - g'(l ± [0.63^/c^]).
THE PROGRESSIVE UNIVERSAL WINDING. The progressive universal winding is a
special type of universal winding in which the wire guide is moved parallel to the axis of
the coil form as the coil winds. The machine for winding this type of coil is usually
equipped with 100 * 1 reduction gears driving the set of gears on the rear of the machine
which produce the progression. The pitch of the winding produced by a 1:1 set of pro-
gression gears is usually very close to 0.01 in., but not exactly so on all machines.
It is necessary to correct the gear ratio (which would be used for an ordinary universal
winding) slightly in order to allow for the change in spacing which results from the pro-
gression. This can be done by reducing g' by the amount — 0.5gpp/c, where gp is the
progression gear ratio and p is the pitch. This factor is usually rather small.
The steps required to determine the winding machine setup for this type of winding
follow:
First, determine the number of turns per inch by dividing the desired number of turns
by the required length. For a relatively wide cam and short winding, it is desirable to
subtract one cam width from the required length for this calculation in order to allow for
the tapering off of the winding at its ends. At this point it is best to examine the result
and determine the number of layers of wire which will be built up radially on the coil.
If the number is less than about 2.5 a solenoid would be preferable; if it is more than about
5 layers, the progressive winding may not build up satisfactorily, and a plain universal
winding of one or more sections may be better.
The cam for a progressive winding is usually as narrow as possible, since the distributed
capacitance and dielectric losses increase with a wider cam. A wider cam, however, de-
creases the steepness of the slope of the pile of wire upon which a turn must be wound and,
consequently, enables a coil having more layers to be wound.
ELECTRICAL DESIGN CONSIDERATION'S 3-35
The value of g' for a progressive winding is usually less than for a universal, since it is
unnecessary to make provisions for winding the coil up to a height comparable to the form
diameter. In this case it is desirable to choose q' and s', again fairly small whole numbers,
but values such as 9/s or 7/n, where qf and s' are larger, produce a better pattern on the
surface of the coil. Landon and Joyner's "composite" winding is obtainable when a fairly
complicated pattern is obtained.
SHIELDING. The successful operation of many of the modern communication lab-
oratory devices and radio receiving sets depends upon the effectiveness of the shielding
between the various parts, and so, in high-gain amplifiers, leads, vacuum tubes, trans-
formers, and tuning coils are all shielded. This process generally requires the placing of a
metallic shielding container around the individual parts. Shielding is attempted against
both electric and magnetic fields and is particularly necessary in circuits carrying high-
frequency currents.
As has been pointed out before, whenever material is brought into the influence of the
electric and magnetic fields of an inductor there is a transfer of energy to that material.
Parts of the inductor are generally at a potential higher than that of the shield, which
is usually at "ground" potential. With this condition there is added to the distributed
capacitance of the winding more capacitance to "ground." This further complicates the
calculation of the actual inductance of the coil at high frequencies.
Shields are generally constructed of non-magnetic or magnetic metals such as iron, zinc,
copper, and aluminum. In the shield used for the shielding of a high-frequency magnetic
field, the efficiency of the screen depends upon the eddy currents produced in the shield.
The energy involved in the circulation of these eddy currents is drawn from the field of
the shielded inductor. Magnetic shielding is therefore always accompanied by an increase
in the effective resistance of the shielded inductor.
When the resistivity and thickness of the metal shield remain constant and the fre-
quency of the alternating electromagnetic field varies, the shielding increases as the
frequency increases, owing to the increased flow of eddy currents. For a given kind of
metal at any specified frequency the shielding efficiency increases as the shield thickness
is increased. Under these conditions, a certain thickness of shield introduces a maximum
resistance into the shielded circuit. The thickness of the shield which gives maximum
added resistance to the shielded circuit decreases as the frequency increases. If shielding
is to be obtained by eddy currents they must be free to flow as they will, which requires
that there be no imperfect joints or breaks in the shield. A short-circuited coil may be
used as a shield since the current induced in it by the field will set up an opposing field
and give a zero local resultant.
In an "open"-circuit electrostatic screen, no eddy currents will flow, and the shield
may be used to prevent the alternating field from reaching an impure dielectric and thus
producing a loss. In this application the shield reduces the effective resistance of the elec-
trical circuit.
Since the eddy currents hi a shield set up a magnetic field opposing the field of the
inductor, it is evident that there will be a reduction of the net field surrounding the in-
ductor winding. There is therefore a change in the effective coil inductance, which
results in a decrease of the inductance value.
Many investigators have attempted to state quantitatively the magnitude of the
screening effects on coil inductance and resistance. An idealized mathematical solution
of the problem (given in the Wireless Engineer] replaces the ordinary cylindrical screen
by a spherical one, and the cylindrical coil by a dipole of the same magnetic moment placed
at the center of the sphere. The development is possible because it has been found that
the exact shape of the screening can is not important, and this permits the mathematical
use of a sphere with a diameter the geometric mean of the three coordinates of the can.
The expression developed shows the reduction of the effective inductance of the coil to
depend upon the frequency, material constants, the screen thickness, and a linear dimen-
sion representing the can size
in which Vc equals volume of the coil (winding section X length); V8 equals volume of
screening can; K equals a constant less than 1 (K = 0.7 when coil length — coil diam-
eter); I/o equals actual inductance of the short solenoid; and a equals factor depending
upon /, dimensions, permeability, and resistivity of the screen can (a — almost 1 for
non-magnetic materials) .
A general interpretation which may be made of this expression is that the effect of the
screen on the coil inductance varies inversely as thja diameter of the screen can to the
cube power.
3-36 RESISTORS, INDUCTORS, CAPACITORS
This conclusion has been stated by Hayman, and the results of a simple expression
of the effect have been accurately checked by experiment. The approximate expression
which has been given for short coils is
(jT}3 _ ££3\
ni j
where D — screen diameter and d — coil diameter. As the coil length approaches half
the can length there is more influence from the ends of the can. This condition requires
the use of a correcting factor which is expressed as
End correction = 1 — ( — - ) (3)
L \2Z can/ J
The calculations with these expressions for coils which do not exceed half the can dimen-
sions have checked experimental measurements within less than 1 per cent.
The effect of the eddy-current flow in drawing energy from the inductor results in an
increase of the effective resistance of the inductor. If skin effect in the shield is negligible
and the eddy currents are uniformly distributed through the screen^ the effective addition
to the coil resistance has been stated as
in which A — cross-section area of coil, square centimeters; T — number of coil turns;
t — thickness of screen, millimeters; r = radius of screen can, centimeters; and p = re-
sistivity of the can material, ohms per cubic centimeter. When skin effect in the shield
forces a non-uniform distribution of eddy current the above expression is modified to
take the form
Rt = 0.95 X 10~4 !TU2 (5)
r4
An indication of the presence of skin effect in the shield is gained from the expression
'V1'
* p
When this factor is less than 5000, the skin effect is negligible.
13. MECHANICAL DESIGN CONSIDERATIONS
FORM MATERIALS. Some of the factors to be considered in choosing a form material
are its mechanical strength, dielectric properties, coefficient of thermal expansion, machin-
ability, moisture absorption, power factor at the operating frequency, and cost. Sometimes
the operating-temperature requirements will not permit the choice of an otherwise desir-
able material, or the heat required to solder leads to lugs on the coil form may soften the
coil form and loosen the solder lugs.
It has been found advisable to select an extremely stable material, whenever frequency
drift requirements are severe, rather than an unstable material with compensation else-
where in the circuit for inductance changes. Glass coil forms are sometimes possible where
only a very small thermal expansion can be permitted. The various kinds of glass, with
coefficients of linear expansion of about 3 to 9 parts per million per degree centigrade, are
among the best materials now available. Steatite and mycalex also exhibit good tempera-
ture stability characteristics.
While phenolic materials have been popular because of their adaptability for use as
form materials and their relatively low cost, their coefficient of linear expansion is only
fair, being about 30 parts per million per degree centigrade.
The coefficient of thermal expansion of materials which are not homogeneous (such as
commercial laminated Bakelite tubing) frequently has different values for the radial and
axial dimensions. Average values of these two coefficients can generally be furnished by
the manufacturer or may be measured directly.
The coil form is usually much more rugged than the winding, and therefore the tempera-*
ture instability of a coil is usually due to its form. Copper wire expands at about the same
rate as Bakelite under varying temperature conditions. However, copper wire can be
wound under tension on one of the more stable form materials and a stable coil will result;
the form, material must be sufficiently stronger than the wire so that the form is not dis-
torted by the pressure of the wire.
MECHANICAL DESIGN CONSIDERATIONS
3-37
Absorption of water by the coil form may result in loss of mechanical strength, a change
in the distributed capacitance of the inductor, and consequent detuning of the circuit,
and may produce conditions favorable to electrolysis or fungus growth. The various
methods of treating coils, such as impregnating, varnishing, or the application of fungi-
cides, may delay these harmful results, but it appears that the most certain way to avoid
them is to choose materials which will not absorb water, if such materials are available
and fulfill the other design requirements.
A partial list of the more important properties of some of the more frequently used form
materials is given herewith.
Typical Properties of Form Materials *
Form
Material
Dielectric
Constant
Power
Factor,
% at 1 me
Maximum
Temperature,
deg cent
Coefficient f
of Linear
Thermal
Expansion
Water
Absorption,
% in 24 hr
Machin-
ability
Bakelite, molded. .
paper base
6.0
5.5
4.0
4.0
120
120
30.0
30.0
0.2
0 2
Fair
Good
Glass
6.0
0.4
Over 500
8.5
0
Very poor
Pyrex ....
4.5
0.2
500
3 5
o
Magnesium silicate
6.0
7 0
0.3
0 3
1000
300
7.0
8 5
0.02
0 04
Very poor
Polystyrene
2 6
0.03
75
70 0
0 01
Good
Porcelain . . ...
6.5
0.7
1000
4.0
0 5
Very poor
Rubber, hard
3.0
1.0
65
75.0
0.01
Fair
* Values given are subject to considerable variation,
f In parts per million per degree centigrade.
IMPREGNATION OF INDUCTORS. Coil impregnation serves two principal purposes:
first, the impregnating material tends to seal out moisture; second, the impregnating mate-
rial improves the mechanical strength of the winding and holds it more firmly in place
on the coil form.
Either before or during the impregnation of the coil, it is necessary to drive out of the
winding and form any moisture that may be present. This is accomplished either by
baking the coil at a temperature slightly higher than 100 deg cent before impregnating or
by maintaining the impregnating material at such a temperature while the coil is being
impregnated. The maximum limit of the temperature used during baking or impregnating
is the temperature that will damage some part of the winding or its form or the impreg-
nating material.
There are many types and mixtures of different types of waxes which are used to im-
impregnate coils. Resins also are mixed with waxes to improve their characteristics.
The melting and softening temperatures, and the hardness of the wax, are determined by
the kinds and amounts of the various kinds of waxes in the mixture. Some mixtures be-
come extremely brittle at fairly low temperatures, which may be a serious disadvantage.
Varnish of good electrical quality, or polystyrene dissolved in a solvent, are sometimes
used to impregnate coils. Vacuum impregnation (dipping the coil in the impregnating
material while it is in a partial vacuum) is usually resorted to when varnish or some similar
material is used to impregnate a coil.
The conditions under which the coil will be used determine the designer's choice of the
method and material for impregnating the coil. Very often the economy of the method is a
determining factor.
Coils which are designed for good conditions of temperature and humidity, such as in
equipment to be used indoors in all but the most humid parts of the United States, are
impregnated usually in a simple and inexpensive way. For instance, many coils are treated
by baking in an oven until most of the moisture is driven out, followed by immersion in a
wax, resin, or mixture of both, at a temperature slightly higher than the boiling point of
water until all agitation of the liquid ceases. The coil is then cooled and finally "flash-
dipped" to produce an even coating of the same or a different impregnant on the outer
surface. The first (baking) operation is frequently omitted for the sake of economy.
Where more severe conditions of temperature and humidity are encountered, some better
methods of impregnation and better materials are required. Two such impregnation
procedures are described below. These methods were developed and tested by the Hazel-
tine Corporation for use on equipment for the Army and Navy during 1945. The two
processes are:
Process 1. Q-Max A-27 diluted 1:1 with Toluene, applied by dipping and baking;
recommended for Silicone-varnished Fibreglas-served wire.
3-38 RESISTORS, INDUCTORS, CAPACITORS
(a) Bake the coil (on its form) for 1 hr at 110-120 deg cent.
(6) While still hot, immerse the coil until bubbling ceases in a solution consisting of:
1 part Q-Max Lacquer A-27
1 part Toluene ("technical grade")
(c) Drain and air dry for 1 hr.
(d) Bake for 4 hr at 140 deg cent.
(e) Apply two more coats per (&) , (c) , and (d) above, redipping immediately after (d) .
Both processes described here require the use of combustible materials. Adequate
ventilation must be provided and safety rules regarding fire hazards observed.
Process 2. Styrene Monomer N-100 and Q-Max A-27 diluted 1 : 1 with Toluene, applied
by dipping and baking. Recommended for use on Fibreglas- or silk-served wire.
(a) Bake the coil (on its form) for 2 hr at 110 deg cent.
(6) While still hot, immerse the coil in styrene monomer for 20 min.
(c) Air dry the coil until dripping ceases.
(d) Bake for 24 hr at 125 deg cent.
(e) Redip in styrene monomer for 20 min.
(/) Repeat (c) and (d).
(g) Apply a thin coat of the Q-Max and Toluene solution.
Coils impregnated according to the two processes given above should withstand tem-
peratures ranging from — 65 to +85 deg cent with the relative humidity as high as 95 per
cent at the highest temperature.
THE SPECIFICATION OF INDUCTORS. The materials and the method of construc-
tion of inductors can be shown readily by means of drawings and written specifications.
However, it is sometimes difficult to specify the performance requirements of an inductor
in an exact fashion. This is due to a lack of standardized measuring equipment in the
industry capable of separating the effects of the distributed capacitance, inductance, and
Q of the inductor in a practical and accurately measurable fashion, especially on the higher-
frequency coils. It is possible, however, to compare one inductor to another with a higher
degree of precision. Therefore, it has become a fairly widely accepted practice for the
designer to adjust accurately one complete set of coils, which become the master standards.
From these master standards, as many secondary standards as are required can be made
and distributed to the coil adjusting and testing points. All performance specifications
requiring very close tolerances are referred to these standards. If the standards are care-
fully prepared, stored, and handled, the variations in their performance over a period of
time due to aging, etc., are minimized. It is desirable to obtain measurements, on the
most stable equipment available, of all possible performance data of the standards so that
the master standards themselves can be rechecked. If both the coil manufacturer and
designer can measure the inductor, with similar equipment and by similar methods, the
data and the inductors measured can be exchanged and the test equipment calibrated alike
in both places. Even if this can be done, in view of the difficulty involved in obtaining
standardized test equipment and conditions it is generally desirable to use the master
standard as the basis of the specification of inductor performance.
14. INDUCTOR DESIGN FORMULAS
The formulas that follow have been found to be generally useful in the design of induc-
tors. The inductance formulas are less accurate than those given in the Bureau of Stand-
ards Circular C74, They do, however, produce a result with approximately the same accu-
racy with which the usual range of radio-frequency inductors can be wound, using materials
which are not selected to closer than normal limits. Their principal advantage is their
simplicity.
The dimensions and symbols used in these formulas follow:
L = inductance of each section of a winding in microhenries.
d — form diameter in inches.
"b — length of winding in inches.
c — throw of cam used to wind a universal section in inches.
w = outside diameter of wire, including covering insulation, in inches.
t = number of turns.
C0 = distributed capacitance in micro-microfarads,
p' = pitch of winding in inches.
h — height of winding above coil form in inches.
a = mean diameter of winding in inches.
INDUCTOR DESIGN FORMULAS 3-39
£,t = total inductance of a multisection universal winding in microhenries.
gp = progression gear ratio.
y =5 number of sections in winding.
g = gear ratio.
g' = pattern gear ratio.
qf — small whole number, numerator of fraction gf.
sf = small whole number, denominator of fraction gf.
z = number of strands in litz wire.
La = apparent inductance in microhenries of coil with distributed capacitance.
o> = 2ir times frequency in megacycles per second.
p — pitch produced by winding machine when 1/1 progression gear ratio is used.
SOLENOID AND PROGRESSIVE UNIVERSAL WINDING. Inductance.
I8d + 406
Accurate to within about 1 per cent for solenoids with b > QAd.
Turns.
t = VL(lSd + 406) (7)
d
Distributed Capacitance.
C° = cosh^ p'/w (8)
for single layer solenoids only, where w is the diameter of the bare wire. The dielectric
constant of the coil form, wire insulation, and impregnating material will increase the
distributed capacitance above the calculated value.
For progressive universal windings, the distributed capacitance is the minimum for the
smallest cam throw; it is approximately proportional to the coil diameter.
EACH SECTION OF A UNIVERSAL WINDING. Inductance.
~ 3d + 9c + 10^
Accuracy to within about 1 per cent when the three terms in the denominator are about
equal.
Turns.
t = log-1 (1.08 - QA7d + 0.16c + 0.5 log L) (10)
to within 5 per cent approximately, for windings having more than about 100 turns. This
is an empirically derived formula. If more accurate results are required, the result may
be substituted in eq. (6) above, and a suitable correction obtained.
Height of Winding.
(11)
for wire which does not flatten appreciably during winding, and with 1.25-wire-diameter
spacing. For litz wire, flattening of the insulation may reduce the calculated height by
about 5 to 10 per cent.
Distributed Capacitance. The distributed capacitance of a universal winding is ex-
tremely variable; it depends upon many factors, including the pattern gear ratio (g')» the
spacing between conductors, etc. It is approximately proportional to the throw of the
cam and to the form diameter. It is fairly independent of the number of turns on the
winding.
MULTISECTION UNIVERSAL WINDING. Inductance.
1/2 = L&y - 1) (12)
approximately, for each section with uniform spacing between sections about equal to
the width of the section.
Distributed Capacitance. Slightly greater than the resultant of the distributed capaci-
tances of the individual sections in series.
SPIRAL WINDING. Inductance.
(d + 7W
16d + 44A
where h is the difference between outside and inside diameters.
(13)
3-40 RESISTORS, INDUCTORS, CAPACITORS
MEASUREMENT FORMULAS. Apparent Inductance.
La = 1 - rfLCo (14)
Distributed Capacitance.
Co = <^ (15)
where Ci and C* are the capacitances required to resonate the inductor at frequencies /
and 2/f respectively. When C\ and C% are large, the value of C0 obtained will be somewhat
larger than that computed from the actual self-resonance of the coil.
FIGURE OF MERIT. The Q of an inductor is usually measured directly on equipment
designed for that purpose. If such equipment is not available, a voltage can be induced
in the inductor in a resonant circuit, with suitable precautions taken to avoid additional
loading, and the resonant band width measured at the half-power point. The ratio of
the test frequency to the distance between the half-power points is equal to the Q of the
inductor.
UNIVERSAL WINDING GEAR RATIO CALCULATIONS
Minimum cam width = Approximately 3w
Cam Cycles per "Winding Cycle.
for forms of average smoothness; this was expressed first by Simon in terms of cross-overs
(one-half cam cycle) per winding cycle:
* - p - 5 (17>
for very smooth forms. Choose a small whole number for q' and s', with
Gear Ratio.
/ n fta*n\
(19)
Set the calculated value of g on the C or D scale of a 10-in. slide rule, and locate the coinci-
dence of two whole-number lines within the range of available gears on the C and D scales.
These two coincident line numbers can be used as the number of teeth in the gears.
PROGRESSIVE UNIVERSAL WINDING GEAR RATIO CALCULATION. To deter-
mine whether progressive universal should be used, if
— < 1 (20)
a solenoid should be used, according to Landon and Joyner. To determine minimum cam
throw:
c > — (21)
gpP
which is Landon and Joyner's formula in the terms used here. To determine cam. cycles
per winding cycle:
g' = — - = i (22)
Choose fairly small whole numbers for qf and s'; the more complicated patterns result
when sf is made fairly large, and a proper choice of qf and sf can be made so that the wire
is adjacent to a preceding turn in the pattern on both forward and backward strokes of
the cam, producing Landon and Joyner's "composite" winding. To determine progression
gear ratio:
gp = j- (23)
To determine gear ratio:
/ 0 Rff^n\ / n fi2in\
(24)
This is essentially the original formula published by Landon and Joyner, in the form sug-
BIBLIOGRAPHY 3-41
gested by Simon. Use the minus sign after gf when the winding forms a right-hand screw
thread. If a left-hand thread is formed, a plus sign should be used. The value of g may
be computed in the same manner as for a universal winding.
BIBLIOGRAPHY
Handbook of Radio Standards, National Electrical Mfr's. Assoc., New York (1928).
Radio Instruments and Measurements, Bureau of Standards Circular 74 (1924).
Morecroft, J. H., Principles of Radio Communication, John Wiley (1933).
Grover, F. W., Additions to the Formulas for the Calculation of Mutual and Self Inductance, Bureau
of Standards Scientific Paper 320 (1918).
Grover, F. W., Formulas and Tables for the Calculation and Design of Single Laver Coil, Proc. I.R.E.,
Vol. 11, 193 (April 1924).
Grover, F. W., Comparison of the Formulas for the Calculation of the Inductance of Coils and Spirals
Wound with Wire of Large Cross Section, Bureau of Standards Journal of Research, Vol. 3, No. 1,
163, Research Paper 90 (July 1929).
Snow, C., Formulas for the Inductance of a Helix Made with Wire of Any Section, Bureau of Standards
Scientific Paper 537 (1926).
Grover, F. W., Methods for the Derivation and Expansion of Formulas for the Mutual Inductance of
Coaxial Circles and for the Inductance of Single Layer Solenoids (includes extensive bibliography) ,
Bureau of Standards Journal of Research, Vol. 1, No. 4, 487, Reprint 16 (October 1928).
Snow, C., The Effect of Small Variation in Pitch upon the Inductance of a Standard Solenoid, Bureau
of Standards Journal of Research, Vol. 6, No. 5, 777, Research Paper 304 (May 1931).
Brooks, H. B., Design of Standards of Inductance and the Proposed Use of Model Reactors in the Design
of Air Core and Iron Core Reactors, Bureau of Standards Journal of Research, Vol. 7, 289, Research
Paper 342 (August 1931).
Rosa, E. B., and Cohen, Louis, Formulae and Tables for the Calculation of Mutual and Self Inductance,
Bulletin of the Bureau of Standards, Vol. 5, No. 1, 1, Tech. Reprint 93 (August 1908).
Rosa, E. B., and Grover, F. W., Formulae and Tables for the Calculation of Mutual and Self Inductance,
Bulletin of the Bureau of Standards, Vol. 8, No. 1, 1, Reprint 169 (January 1912).
Snow, C., Simplified Precision Formula for inductance of a Helix with Lead-in Correction, Bureau of
Standards Journal of Research, Vol. 9, 419 (September 1932).
Wheeler, H. A., Simple Inductance Formulas for Radio Coils, Proc. I.R.E., Vol. 16, No. 10, 1398
(October 1928).
Brainerd, J. G., Inductance at High Frequencies and Its Relation to the Circuit Equations, Proc. I.R.E.,
Vol. 22, No. 3, 395 (March 1934).
Palermo, A. J., Distributed Capacity of Single Layer Coils, Proc. I.R.E., Vol. 22, No. 7, 897 (July 1934).
Palermo, A. J., Effect of Displacement Current on Radio Frequency Resistance of the Single Layer
Coil, Proc. I.R.E., Vol. 20, No. 11, 1807 (November 1932).
A Critical Review of Literature on Amplifiers for Radio Reception, Radio Research Special Report 9,
Department of Scientific and Industrial Research, published under the authority of his Majesty's
Stationery Office, London (1930).
Breit, G., Some Effects of Distributed Capacity between Inductance Coils and the Ground, Bureau of
Standards Scientific Paper 427. Scientific Papers, Vol. 17, 521 (December 1921).
Hickman, C. N., Alternating Current Resistance and Inductance of Single Layer Coils, Bureau of
Standards Scientific Paper 472, Scientific Papers, Vol. 19, 73 (May 1923).
Breit, G., The High Frequency Resistance of Inductance Coils, Bureau of Standards Scientific Paper 430,
Scientific Papers, Vol. 18, No. 17, 569 (1922).
Butterworth, S., Effective Resistance of Inductance Coils at Radio Frequency, Experimental Wireless.
Vol. 3, 203, 267, 417, 483 (1926).
Austin, B. B., Effective Resistance of Inductance Coils at Radio Frequency. An abstract of a paper
by. S. Butterworth (see above), Wireless Engineer, Vol. 11, No. 124, 12 (January 1934).
Palermo, A. J., and Grover, F. W., Study of High Frequency Coil Resistance, Proc. I.R.E., Vol. IS,
No. 12, 2041 (December 1930) ; Vol. 19, No. 7, 1278 (July 1931).
Hund, August, High Frequency Measurements, International Series in Physics, McGraw-Hill (1933).
Hund, A., and DeGroot, H. B., Radio-frequency Resistance and Inductance of Coils Used in Broadcast
Reception, Bureau of Standards Technical Paper 298, Vol. 19, 651 (1925).
Hall, E. L., Resistance of Conductors of Various Types and Sizes as Windings of Single Layer Coils at
150 to 6000 Kilocycles, Bureau of Standards Technical Paper 330, Vol. 21, 109 (1926).
Barden, W. S., and Grimes, D., Coil Design for Short Wave Receivers, Electronics, Vol. 7, No. 6, 174
(June 1934).
Brown, W. W., and Love, J. E., Design and Efficiencies of Large Air Core Inductances, Proc. I.R.E.,
Vol. 13, No. 6, 755 (December 1925).
Effect of Screening Cans on Effective Inductance and Resistance of Coils, Wireless Engineer. Vol. 11,
No. 126, 115 (March 1934).
Hayman, W. G., Inductance of Solenoids in Cylindrical Screen Boxes, Wireless Engineer, Vol. 11, No.
127, 189 (April 1934).
Pollack, D., and Hartley, M., Short Wave Coil Characteristics, Research Labs., Columbia University
(1935). - 8
Simon, A. W., Winding the Universal Coil, Electronics, Vol. 9, 22 (October 1936).
Joyner, A. A., and Landon, V. D., Theory and Design of Progressive Universal Coils, Communications,
Vol. 18, 5 (September 1938).
Hershey, L. M., The Design of the Universal Winding, Proc. I.R.E., Vol. 29, 442 (August 1941).
Simon, A. W., On the Winding of the Universal Coil, Proc. I.R.E., Vol. 33, 35 (January 1945).
Simon, A. W., On the Theory of the Progressive Universal Winding, Proc. I.R.E., Vol. 33, 868 (Decem-
ber 1945).
Terman, F. E,, Some Possibilities for Low-loss Coils, Proc. I.R.E., Vol. 23, 1069 (September 1935).
Reber, G., Optimum Design of Toroidal Inductances, Proc. I.R.E., Vol. 23, 1056 (September 1935).
Pollack, D., The Design of Inductances for Frequencies between 4 and 25 megacycles, RCA Review,
Vol. II, 184 (October 1937), and Electrical Engineering, September, 1937.
3-42
RESISTORS, INDUCTORS, CAPACITORS
FERROUS-CORED INDUCTORS
By A. J. Rohner
The utility of ferromagnetic cores in coils lies in the fact that such cores have a higher
magnetic permeability than air. This permeability may be anywhere between 2 and
100,000. The use of a ferrous core may have the following beneficial effects:
(a) Increase of inductance. With a complete magnetic path of ferromagnetic material,
this increase may be several thousand times the air-core value of inductance.
(6) Increase of Q. This results from the increased inductance, if the increase of loss
due to core loss is not greater than the increase of inductance.
(c) Magnetic shielding. The magnetic field of the coil is constrained to follow to a
large extent the path of the high-permeability core.
(d) Adjustability of inductance. Movement of the core in or out of the coil, or variation
of an air gap in the core, gives mechanical means of adjusting the inductance.
The limitations of ferromagnetic cores in coils are due to certain undesirable qualities of
ferromagnetic materials. Most important of these are:
(a) Magnetic saturation, which occurs at 7000 to 15,000 lines per square centimeter.
These values depend upon the kind of core material and are for a magnetizing force of
10 oersteds.
(Z>) Non-constant permeability. Permeability varies with the direct current passing
through the coil, the alternating voltage impressed across the coil terminals, and other
factors.
(c) Core loss, which is a wattage loss additional to the copper loss of the coil; it deter-
mines the frequency range for which each type of core material may be used.
Core loss consists of two distinct parts, hysteresis loss and eddy-current loss. See
Section 2, "Magnetic Materials," Spooner, "Properties and Testing of Magnetic Mate-
rials," or "Magnetic Circuits and Transformers" by staff of M.I.T. Hysteresis loss is a
magnetic effect due to the magnetizing and demagnetizing of the core and is proportional
to the frequency. Hysteresis loss can be reduced by using core material that is easily
magnetized and demagnetized, i.e., a "magnetically soft" material. Eddy-current loss
is an electrical effect due to induced currents within the core material and is proportional
to the square of the frequency. Eddy-current loss can be reduced by using core material
of high electrical resistivity, and by laminating or powdering the core.
At the higher frequencies, eddy-current loss becomes predominant and a finer subdivision
of the core material is necessary. ^
Frequency Ranges. At frequencies below about 4 kc, the core usually consists of thin
sheets, either in the form of fiat plates or "laminations," as thin as 0.003 in., or in the form
of ribbon, which can be made as thin as 0.001 in. Above 20 kc, the core usually consists
of powdered material, the grains of which may average as little as 0.00012 in. in diameter.
Between 4 and 20 kc, either sheet material or powdered material may be suitable. How-
ever, thin ribbon cores are useful up into the low- and medium-radiofrequency bands,
while powdered cores, of larger grain size, are useful down to 1 kc or lower.
15. LOW-FREQUENCY, SHEET-CORE INDUCTORS
(a)
Scrap Less El
Strapless
(6)
Strapless EE
FIG. 1.
W
Strapless
Ribbon core
Laminations and Ribbon Core
CORE CONSTRUCTION.
Typical lamination shapes,
and a ribbon core, are shown
in Fig. 1. In general, all
sheet-material cores form a
complete magnetic path
around the coil, except for
small air gaps which may be
purposely introduced, and the
cross-section of this magnetic
path is essentially uniform
throughout the length of the
magnetic circuit.
Assembly of laminated
cores is illustrated in Fig. 2.
A butt joint is actually a
small air gap, because of oxide
on the ends of the lamina-
LOW-FREQUENCY, SHEET-CORE INDUCTORS
3-43
tions, non-squareness of the ends, and imperfect meeting of the joint. This butt-joint
gap may be from 0.0005 to 0.002 in. long. A value of 0.0015 in. per gap may be assumed
for average design purposes. When there is an air gap, the magnetic flux usually must
cross this separation twice. Thus, for example, if the air-gap spacer is 0.010 in. thick,
the total length of air gap in the core, including the butt-joint gaps, is 0.023 in.
Usually, ribbon cores are cut in two after winding, forming two C-shaped pieces, and
the ends of each C-piece are ground flat. When the two pieces are placed together, after
adding the coil, the ends meet in tight butt joints,
each joint being about 0.0005 in. long, so that the core ^^H^^ Cross
as a whole approaches a continuous ferromagnetic *^^s§§^s. section
path.
Stacking Factor. Because of oxide or other insula-
tion on the sheet material, non-flatness of sheets, and
stamping burrs on laminations, the magnetically use-
ful cross-section of a sheet core is never 100 per cent
of the measured cross-section. The ratio of the two
is called the "stacking factor." Values that may be
used as a guide are given in Table 1. Interleaved
Mean length of
magnetic path
Table 1. Stacking Factors
Laminated Cores
Ribbon Cores
19-mil
1 4-mil
6-mil
3-mil
0.94
0.92
0.83
0.71
14-mil
5-mil
3-mil
2-mil
0.65
0.91
0.86
0.80
Air-gap
Materials most commonly used in sheet-material
cores are: Button! Air gap
(a) Silicon steel, especially the better grades, having FIG. 2. Assembly of Laminated Cores
silicon content from 2.5 to 4.75 per cent.
(6) Grain-oriented silicon steel. Hipersil and Silectron are trade names for this material.
(c) Nickel-iron alloys, of approximately 50-50 composition, variously known as Nicaloi,
Hipernik, 4750, or 49- Alloy.
(d) Permalloy, an alloy of about 80 per cent nickel with iron. Hymu is a similar
material.
(e) Mumetal, similar to permalloy, but with 5 per cent copper added.
For more detailed description of sheet-core materials, see Section 2, Magnetic Materials,
Spooner, Chapter IV; Elmen, "Magnetic Alloys of Iron, Nickel, and Cobalt," /. Franklin
Inst., May 1929; Alleghany Ludlum Bulletins EM-11 and EM-12, and then- Magnetic
Core Materials Practice; Follansbee, Electrical Sheet Handbook, Magnetic Metals High
Permeability Alloys; and Westinghouse, Metals and Alloys.
Thickness of Sheets. For inductors operating at 25 to 120 cycles, 25-mil-thick (U.S.S.
gage 24) and 19-mil-thick (26-gage) laminations are useful. Sheet of 14-mil thickness
(29 gage) is widely used, both for laminations and ribbon, for applications from 60 cycles
to the middle audiofrequencies. Below 14 mils, sheet material can be obtained in almost
any thickness down to 1 mil. However, stamped laminations, and preformed ribbon cores,
of these thinner sheets became available largely as a result of war needs and are not yet
standardized. Laminations can be purchased, of 7-
mil silicon steel, 6-mil 49-Alloy and Hymu, 4-mil 4750,
and 3-mil 4750, in a large variety of sizes. Hipersil
ribbon cores are obtainable in 14-, 5-, 3-, 2-, and 1-mil
sheet thickness.
COIL CONSTRUCTION. Low-frequency induc-
tors usually have multilayer coils, with insulation
between layers. See Fig. 3. The coil is wound upon
a rectangular spool of spirally wrapped paper or fiber,
30 or 40 mils in total thickness, slightly larger in inside
dimensions than the core over which it is to be placed,
and slightly shorter than the core window. These
clearances may be */32 or Vie in. Wire is usually solid
copper, with enamel insulation. The length of the
winding, or "wire traverse," is less than the length of the spool, to allow a "margin"
of 3/32 to 3/ie in. at either end. Over each layer of wire is placed one turn of insulation,
the same width as the length of the spool, which forms a smooth support for the next
layer. Kraft paper, having a thickness about Vs of the wire diameter, is a very satis-
Layer Insul;
Spool.
artfn
Start of cofl
Start of second layer
FIG. 3. Layer-wound Coil
3-44 RESISTORS, INDUCTORS; CAPACITORS
factory material for layer insulation. Glassine paper, of about the same thickness, is
often used with wire of 24-gage (A.W.G.) or smaller. Layer-wound coils, of this con-
struction, require no end boards to hold the wires in place.
Coils without layer insulation (random-wound) may also be used, allowing about 50
per cent more turns in a given space. There are several disadvantages to this type of
winding, however. The wire must have more than ordinary enamel insulation to prevent
shorted turns, which reduces the space advantage somewhat. End boards, or tape, are
necessary to hold the wires in place. Multiple winding cannot be used.
After the coil is wound, flexible lead wires are attached if the wire of the coil is smaller
than 20 gage. Then the coil, or the core and coil together, are impregnated with a varnish.
wax, or asphaltic compound to exclude moisture and air and to strengthen the coil mechan-
ically. See Belden Handbook 12, Anaconda "Magnet Wire and Coils," or Inca Bulletin 3.
Inductors having a three-legged core, Fig. 1 (a) , (6) , (c) , have a single coil, placed on the
middle leg of the core. With two-legged cores, Fig. l(d), (e), (/), two coils are sometimes
used, one on each leg, the two coils being connected in series or in parallel. The use of
two coils results in lower resistance and a smaller dimension over the coil.
DESIGN PROCEDURE is carried out by:
(a) Choosing a core material and core size.
(6) Choosing a wire size, and determining how many turns of this wire will fit in the
core window. About 5 per cent allowance should be made for wires not lying tightly
together. Also, the total calculated build of the coil, including spool, layer insulation, and
outside wrapper, should not exceed 90 per cent of the core window height.
(c) Calculating the inductance, resistance, core loss, heating, capacity, and Q from the
dimensions and the number of turns. Three or four trial designs may be necessary before
the desired constants are arrived at.
Inductance. Since sheet material cores are characterized by high permeability, prac-
tically all the magnetic flux is confined within the core structure. The inductance of a
sheet-core inductor, without air gaps, is given by
x 10- henry (1)
in which N is the number of turns on the .coil, A is the cross-section of the core in square
centimeters, k is the stacking factor, I is the mean length of the magnetic circuit in centi-
meters, and juac is the a-c, or "incremental," permeability of the core material.
When air gaps are present in the core, the inductance is given by
g x 10-» henry (2)
in which ^avg is the average permeability of the core, including air gaps, This average
permeability is
Mavg — -, , /_/7^ - (3)
in which a is the total effective length of all air gaps, in centimeters.
At any air gap the magnetic flux spreads, so that the cross-section of the magnetic field
is greater than the cross-section of the core. It is most convenient to treat this "fringing"
as if the length of the air gap were effectively reduced. If m and n are the dimensions of
the core cross-section at the air gap, and lg is the actual physical length of the air gap,
Effective length — - - — — — — — X lg approximately (4)
(m + lg) (n + lg)
Permeability. Incremental, or a-c, permeability is the kind of permeability of interest
in connection with most inductors. See Magnetic Circuits and Transformers, p. 198. It
is a variable, depending upon:
(a) The material of the core.
(6) The amount of d-c magnetization,
(c) The amount of alternating flux.
(d) Wave form of the a-c voltage.
(e) Previous magnetization of the core.
(/) Temperature.
Of these factors, only the first three are considered in practical design work, although the
others are by no means negligible.
When a core has no air gaps, the d-c magnetization, H^c, is given by
jETdc = ~~~l - oersteds (or gilberts per cm.) (5)
in which I is the direct current flowing through the coil, in amperes.
LOW-FREQUENCY, SHEET-COEE INDUCTORS
3-45
It is usually more convenient to express the amount of a-c magnetization of the core in
terms of flux-density variation, which is a function of the a-c voltage across the coil, rather
than in terms of magnetizing force, which is a function of the a-c current in the coil. The
peak a-c flux density, -Bmax, is given by eq. (6), if the a-c voltage is sinusoidal.
E
X 10s gausses
(6)
In this equation, E is the rms voltage across the coil, / is the frequency, and the other
symbols have the same meaning as 10000
given previously for eq. (1). Equa- ' r
tion (6) applies whether or not there
are air gaps in the core. See Figs.
4, 5, and 6.
D-c Magnetization with Air Gaps.
D-c magnetization can be reduced by
inserting an air gap in the core, im-
proving the a-c permeability. See
Figs. 4, 5, and 6. Up to a certain
point, this results in an increase of
inductance. See eqs. (2) and (3).
Beyond that point, any further in-
100
10 20 50 100 500 1000
A-c Flux density, Bmax, In gausses
FIG. 4. A-c Permeability 3.6% Silicon Steel "58" Grade
10,000
crease in the air gap causes a de-
crease of inductance.
The amount of d-c magnetization
in the ferromagnetic core material, when there is an air gap in the core, can be determined
by the graphical method shown in Fig. 7. See Karapetoff, The Magnetic Circuit. This
method utilizes the normal magneti-
20,000 i 1 i i i i mi i i i i 1 1 in 1 ^r i *KJ 1 1 1 1 r zation or B-H curve of the particular
core material, of which several are
given in Fig. 8.
The d-c magnetization of the core
material and the a-c flux density
[eq. (6)] having been determined,
the a-c permeability is then found
from curves such as Figs. 4, 5, or 6.
This value of permeability is used
in eq. (3) to compute the average
permeability of the core, including
air gaps, which is then used in eq. (2)
to calculate the inductance of the
reactor. It is usually necessary to
try two or three values of air gap
to discover the optimum one. This
method of determining the optimum
air gap, and the maximum inductance, may be called the "fundamental method."
A short-cut method of determining optimum air gap and maximum inductance was
worked out by C. R. Hanna (De- 2o 000
sign of Reactances and Transform-
ers Which Carry Direct Current,
Trans, A.I.E.E., February 1929).
He showed that a curve can be
drawn, for any particular core ma-
terial, whose coordinates are NI/l
and LI2/V, V being the volume of
the core. Such "optimum design
curves" are shown for three com-
monly used materials in Figs. 9,
10, and 11. When using these
curves it should be remembered
that they apply only to a special
case, in which maximum induct-
ance for a given amount of direct
current is the quality desired. If
200
100
10 20 50 100 500 1000 10,000
A-c Flux density, Bmax, in gausses
FIG. 5. A-c Permeability 50-50 Nickel-iron Alloys
10,000
5000
3000
2000
1000
the reactor is to be used at several
different values of direct current,
100 200 500 1000
A-c Ftux djenslty, Bmax, in gausses
2000
FIG. 6. A-c Permeability Mumetal
3-46
RESISTORS, INDUCTORS, CAPACITORS
or if other considerations govern the design, the approach described previously should
be used.
Saturation. If the sum of the d-c flux density and the peak a-c flux density approaches
the saturation density of the core material, serious wave-form distortion occurs. This sum
° (gausses)
itization.
itralght line
(oersteds)
Q.47TNI
FIG. 7. Graphical Method of Determining
D-c Magnetization of Core, when there is an
airgap
12345
H magnetizing force in oersteds
FIG. 8. D-c Magnetization Curves
should not exceed 12,000 gausses for silicon steel or for 50-50 nickel alloys. The d-c flux
density may be found by the graphical method of Fig. 7, and the peak a-c flux density,
0.0026
0.0024
0.0022
0.0020
0.0018
0.0016
LI20.0014
v
0.0012
0.0010
0.0008
0.0006
0.0004
0.0002
0
0.0 4^
<
i /T
//
^
o.oc
m
003
%
'i
0.0
K"
0.0
025
^
A ?-00
20V
7f.cc
30
* 0.0015,/
D02!
.
/
^
•« r\
320
D.OO
10X
' ^
^
/
/
/ 0
001
5
UUOj
{S
"o.c
010
But
: joir
^f*C
.00
15
^
^
Butt joint.
Dim
ensii
>ns i
i ce
itim<
ters
0 5 10 15 20 25 30 35
NI/Z
FIG. 9. Optimum Design Curves for Inductance with D.C. 3.6% Silicon
-Bmax, from eq. (6) . If the total flux density is excessive, and the d-c flux density is the
larger part, the air gap should be increased. If the a-c flux density is the larger part, the
number of turns on the coil should be increased.
LOW-FREQUENCY, SHEET-CORE INDUCTORS
3-47
0.0030
0.0028
0.0026
0.0024
0.0022
0.0020
0.0018
II!
V 0.0016
0.0014
0.0012
0.0010
0.0008
0.0006
0.0004
0,0002
0
H
04,
04
003
0
7,
i
R
nax
gau
=100
sses
003
A
/t
X).C
035
V
-«,
^
O.OC
25 ,
//\™\
33
,°*
y^
Trax
gau£
=10
ses
3
<,
^ 0
002
'vo
002
^
/<
y
n or
.00
f5X
r
.00:
^0
001
5
^
3.00
35
/"
o.oc
r
$
1.00
^
But
join
iX
^
/[But
:|o!
ilt
1
Dim
ms
ns
i cer
tlm
ters
3 5 10 15 20 25 30 35
NI/Z
FIG. 10. Optimum Design Curves for Inductance with D.C. 50-50 Nickel-iron Alloys
0.0038
0.0036
0.0034
0.0032
0.0030
0,0028
0,0026
0.0024
0.0022
V 0.0020
0.0018
0.0016
0.0014
0.0012
0.0010
0.0008
0.0006
0-0004
0.0002
0
C
xoossyj |
\//
X
~
303
^
0-0
330
/
•X
^
/<£
f o.oos
5/
^
^0
003
3
/
/
C?
/
/
0.0
D20
/
/o.
302,
)
/
/
//
0
001
y
/o
.002
0
/
y
0.0
310
//
0.0
015
/,
/
-O.C
nop
/
r °
.00:
0
A
K
o.oc
tt Jo
^
^BL
poo
int
Dim*
nslo
ns ir
cen
time
:ers
) 5 10 15 . 20 25 30 3E
NI/Z
FIG. 11. Optimum Design Curves for Inductance with D.C. Hipersil
3-48
RESISTORS, INDUCTORS, CAPACITORS
RECTIFIER-FILTER REACTORS AND AUDIOFREQUENCY PLATE REACTORS
are examples of inductors for which maximum inductance at a given value of direct current
is the most important quality desired. The "optimum design curves" are ideally suited
for such designs.
THE SWINGING CHOKE is a reactor which must have a specified inductance at some
large value of direct current, but which must increase rapidly in inductance as the direct
current is decreased. An air gap is used which is optimum, not for the largest direct cur-
rent nor for the smallest direct current, but rather for some intermediate value. An ap-
proximate design can be arrived at by using the "optimum design curves" for an interme-
diate value of direct current. Then the inductance should be calculated for the maximum
and minimum currents by the fundamental method. In some
cases, part of the core stack may have a large air gap to
provide a good inductance at the largest current, while the
remainder of the core may have a small air gap to give high
inductance at the minimum current.
SATURABLE REACTORS are inductors the inductance of
which is varied by means of a variable direct current. Inter-
leaved laminations are used to get the greatest effect of the
d-c magnetization. It is necessary to isolate the d-c circuit
from the a-c circuit by means of separate windings. It is also
necessary to prevent transformer coupling between the a-c
and d-c windings. Figure 12 illustrates the construction of
a saturable reactor. The a-c windings should always be
See Holubow, "D-C Saturable Reactors for Control Purposes,"
A-c
n
__7
circuit
LJ
— '
\
Interleaved core
D-c circuit
FIG. 12. Construction of
Saturable Reactor
connected in parallel.
Electronic Industries, March 1945.
COIL RESISTANCE. The mean length of turn is calculated from the coil geometry,
converted into feet, and multiplied by the number of turns. Reference to a wire table
(Section 2, article 3) will give the d-c resistance of the coil, in ohms. Skin effect can be
neglected, except for very large wire, above 1 kc. Allowance for temperature must be
made. The resistance of a coil increases about 0.4 per cent per degree centigrade, above
20 deg cent. Thus, if an inductor operates
at a coil temperature of 70 deg cent, its
resistance will be 20 per cent higher than
calculated for 20 deg cent.
CORE-LOSS curves are shown in Sec-
tion 6, article 14. The core loss is deter-
mined in watts, which can then be added
to copper loss watts to find the total heat
dissipated in the reactor, and the tempera-
ture rise.
When the effect of core loss on the Q
of the inductor, rather than heating, is the
matter of interest, core loss can be repre-
sented by a resistor in parallel with the
coil, of a value Ri ohms.
W
(7)
1
-o
e;
a
a.
V)
0.1
— J
"7
t-
//
^
i
//
^
/
sff
/
/
J
^
|v
/
r"
/
^
5
i
i^^zz
>v /
*s
I
N'
sr /ff
^•j
*!/
N
/j
/
r /
xf<
/"V
f
0.01
5
/f/~
7~7
/ /
/
/
/ //
/x
^
*/
0
100 1000 10,000
In this formula, E is the rms voltage
across the coil, and W is the watts core
loss. The core loss of most sheet-core
materials varies very nearly as the square
of the applied voltage, so that the ratio
E2/W is very nearly constant over a con-
siderable range of voltage. Figure 13
gives core-loss curves of several materials
at 2000 gausses. If P is the watts per
pound, at 2000 gausses, and M is the weight of the core, in pounds, the core-loss resistance is
Cycles per aecond
FIG. 13 Core Loss at 2000 Gausses CBmax)
3~10 ohm
(8)
OPTIMUM Q. Q is often defined as the ratio of reactance to resistance. This is true
when the only resistance present is in series with the coil, as is the case with the copper
resistance of the winding. When there are both series and shunt resistances, as with a
LOW-FREQUENCY, SHEET-CORE INDUCTORS 3-49
ferrous-cored inductor, Q is more clearly defined as the ratio of reactive volt-amperes to
resistive volt-amperes.
For a particular core and coil, at a particular frequency, the shunt resistance of the
core and the series resistance of the coil are practically fixed quantities. The reactance,
however, can be varied by changing the air gap. There is a value of reactance which will
produce the maximum Q. This problem is illustrated by the circuit shown in Fig. 14. In
this circuit, Rc is the resistance of the coil, Ri is the resist-
ance of the core, and X is the reactance of the inductor.
Maximum Q is attained when CoU resistance j
•^-^ or X = VRJ2i (9) Ri|
•"'C -^ Core-loss 1
resistance^
The air gap is adjusted so that
X
Col!
reactance
27T/
for maximum Q
(10) FIG. 14. Equivalent Circuit,
Ferrous-cored Inductor
Equations (2) and (3) are used to compute the correct air gap. When the air gap and
inductance are adjusted to optimum,
V
The maximum Q that can be obtained in a low-frequency, sheet-core inductor is prac-
tically independent of the inductance, the number of turns, the voltage, or the flux density.
That is, a 10-henry reactor can be made with practically the same Q as a 1-mh. reactor,
by proper design. Maximum Q that can be realized depends only on the core material,
the size of the core, and the frequency. See Fig. 15. For other sizes of core, the Q will
10
200
5000 10,000
500 1000 2000
Cycles per second
FIG. 15. Q vs Frequency, Various Core Materials
vary as the linear dimension if the proportions are the same, or as the cube root of the core
volume if the proportions are different. Thus, a core having twice the linear dimensions
of the one shown will have 8 times the volume but will give only twice the Q. For other
core materials, the Q that can be realized will vary inversely as the square root of the
relative core loss. Thus, a material having one-fourth the core loss will give twice the Q.
Air Gaps for Q should be located inside the coil, and preferably at the center of the coil
length. There should be no air gaps outside of the coil. Fringing flux creates a magnetic
field external to the reactor. When the reactor is placed in a metal can, or near a metal
chassis, eddy currents are set up, which may reduce the Q of the reactor by a factor of
2 or 3 to 1.
Optimum Permeability for Q. For a particular core and coil, at a particular frequency,
there is an optimum value of inductance which will give the highest Q. See eq. (10) . This
value of inductance requires a certain average permeability of the core. See eq. (2).
3-50
RESISTORS, INDUCTORS, CAPACITORS
1000
Practically all sheet-core materials have too high a value of a-c permeability to give the
optimum inductance, so that it is necessary to reduce the overall permeability of the core
by inserting an air gap. The use of an air gap to produce maximum Q in an inductor
should not be confused with the use of
an air gap to reduce d-c magnetization.
The two purposes are different and dis-
tinct.
The optimum overall permeability,
Pavg, required to produce maximum Q is
a function of the core material, the core
size, and the frequency. See Fig. 16.
For other sizes of core, optimum perme-
ability will vary inversely as the linear
dimensions if the proportions are the
same, or inversely as the cube root of the
core volume if the proportions are dif-
ferent. For other core materials, the
optimum permeability will vary in-
versely as the square root of the relative
10,000 core loss.
A striking fact brought out by Fig. 16
is that the optimum overall permeability
becomes less than 50 at frequencies
50 100
FIG. 16.
1000
Cydes per second
Permeability for Maximum Q
above 4000 cycles. The high a-c permeability characteristic of sheet-core materials is of no
advantage in this region. Permeability of the order of 50 can be realized with powdered-
iron cores. This opens up the possibility of using powder cores at such frequencies.
16. HIGH-FREQUENCY, POWDERED-CORE INDUCTORS
Powdered cores differ from sheet cores in two important characteristics. They have,
in general, lower core loss, particularly eddy-current loss, and they have much lower
permeability. Both these characteristics are due to the subdivision of the core into minute
particles, and both are desirable at high frequencies if the Q of the inductor is a major
consideration. See above, "Optimum Permeability," and Fig. 16.
Material used for powdered cores are magnetite, a natural iron oxide, electrolytic iron,
hydrogen-reduced iron, carbonyl iron, powdered Permalloy, and powdered molybdenum
Permalloy. For descriptions of these materials and their method of manufacture, see
Section 2, "Magnetic Materials"; H. G, Shea, "Magnetic Powders," Electronic Industries,
August 1945; V. E. Legg and F. J.
Given, "Powdered Molybdenum
Permalloy," B.S.T.J., July 1940.
Particle sizes range from about 50
microns diameter (0.002 in.) for audio-
frequency cores to about 3 microns for
cores useful at 100 me. The particles
making up a core are not all the same
size. This is an advantage, as it gives (a\ R^ core tc\ SIu
a better packing of the magnetic mate-
rial, the smaller particles filling in the
spaces between the larger ones. Since
eddy-current loss is proportional to the
square of the particle diameter, the
root-mean-square diameter of the par-
ticles making up a core is the particle
dimension of greatest significance.
Weight-average diameter is often
given. This is a figure a few per cent
higher than the root-mean-square di-
ameter.
(d) Core arrd shell (e) Oore and half shaQs
FIG. 17. Basic Types of Powdered-iron Cores
CORE CONSTRUCTION. Particles are coated with an insulating material, or treated
in some manner to give them high surface resistivity, and mixed with a plastic binder.
The mixture is compressed in molds at pressures of 50 to 100 tons per square inch, to form
the desired core shape. The resulting core is a solid block of material resembling iron in
appearance and somewhat lighter than iron in weight. Figure 17 illustrates a few basic
HIGH-FREQUENCY, POWDERED-CORE INDUCTORS 3-51
styles. As better audiofrequency core materials are developed, cores of the shapes shown
in Fig. 1 are also being offered.
COIL CONSTRUCTION, in general, follows the practice used for air-core coils of the
same frequency range. Since powdered-iron cores are employed at the higher audio-
frequencies and above, skin effect, coil capacitance, and coil dielectric loss are controlling
factors in coil design, as with air-core coils. See Section 2, "Inductors with Air Cores."
The presence of a core introduces two modifications of coil design. A somewhat longer
coil, of less build-up, is desirable, to take better advantage of the core. Dielectric loss and
dielectric constant of the winding form are of more importance when there is a core,
especially if the core is grounded.
PERMEABILITY. "Intrinsic permeability" is the permeability of the magnetic
particles. "Composite permeability," "ring-core permeability," or just "permeability''
are terms used to describe the permeability of a core, made in the form of a ring sample,
and wound with a toroidal coil. Such a sample has uniform flux density throughout its
length and practically throughout its cross-section, and no end effects. Consequently,
the ring-core permeability may be called the true permeability of the core material. The
relation between ring-core permeability, ju, and intrinsic permeability juz-, is given by
M « (Mf)p (12)
in which p is the "packing factor," or fraction of the core volume occupied by magnetic
material. See Legg and Given, also analysis by H. Beller and G. O. Altmann, "Radio-
Frequency Cores of High Permeability," Electronic Industries, November 1945. Table 3
gives values of ring-core permeability for a number of core materials.
The term "effective permeability" is used to describe the permeability of a cylindrical
or slug-type core [Fig. 17(&)]. Such permeability is much lower than ring-core permeability
of the same core material, be-
cause of demagnetizing effects
at the ends of the cylinder.
This matter has been investi-
gated by R. M. Bozorth and
D. M. Chapin, "Demagnetiz-
ing Factors of Rods," J. Ap-
plied Phys., May 1942, and
by W. J. Polydoroff and A. J.
Klapperich, "Permeability of
High Frequency Iron Cores,"
Radio, November 1945. Ta-
ble 2 shows effective perme-
ability versus ring-core per-
meability for various ratios of
core length to core diameter.
INDUCTANCE.
Table 2. Effective Permeability of Cylindrical Cores
Ring-core
Permeability
Ratio Length/Diameter
1
2
4
6
8
Effective Permeability
5
10
15
20
25
30
2.20
2.98
3.47
3.76
3.94
4.06
3.40
4.57
5.65
6.3
6.6
6.75
4.1
6.8
8.7
9.9
10.6
11.0
4.4
8.2
10.8
12.4
13.4
14.0
4,8
8.8
11.7
13.7
14.8
15.6
The coil is the same length as the core, in these data.
The inductance of a toroidal coil on a ring core is given by
4. AT2
=j
a
.
~=j-[A' + A.(p - 1)] X 10'fl henry
(13)
in which N is the number of turns on the coil; d is the mean diameter of the core, in centi-
meters; A' is the mean cross-section of the coil, at right angles to the flux path, in square
centimeters; A is the cross-section of the core, in square centimeters; and AC is the ring-core
permeability of the core.
The inductance of a coil on a cylindrical, or slug-type core, if the coil is the same length
as the core, is
In this equation, Z/o is the inductance of the coil without iron, 6t- is the radius of the iron
core, 60 is the mean radius of the coil, and p* is the effective permeability, as given in
Table 2. If the core is longer than the coil, the effective permeability is increased to a value
At.'
(15)
k being the length of the core, and Z0 that of the coil. This higher value should be sub-
stituted for ne in eq. (14) .
Formulas are not available which apply to the various shell-type cores. The variety
of shapes, non-uniform cross-section of the core, and square corners in the magnetic path
3-52
RESISTORS, INDUCTORS, CAPACITORS
offered by the core make any accurate analysis very difficult. The inductance of a coil,
having a central core and a shell, will be greater than its inductance with the central core
alone. On the other hand, its inductance will be less than that of a toroidal coil, of the
same number of turns, on a ring core of the same average cross-section and the same mean
length of magnetic path. See "Measurement of Iron Cores at Radio Frequencies," D. E.
Foster and A. E. Newlon, Proc. I.R.E., May 1941, and above reference by Polydoroff and
Klapperieh.
CORE LOSS AND Q. Core loss is of interest in high-frequency inductors primarily
because of its effect upon Q, or quality factor. The addition of the core increases not only
inductance but also resistance. A toroidal coil on a ring core has been analyzed by V. E.
Legg, "Magnetic Measurements at Low Flux Densities," B.S.T.J., January 1936. His
formula for the increase of resistance due to core loss is
R = [(aBm + c)/ +
ohms
(16)
In this, R is the resistance added to a coil by the core; a, c, and e are the hysteresis, residual,
and eddy-current loss coefficients; /is the frequency, in cycles per second; Bm is the peak
a-c flux density, in gausses; /x is the ring-core permeability; and L is the inductance of the
coil with the core, in henries. Coefficients are given in Table 3 for a number of core
materials.
The resistance added to a coil by a cylindrical core has been analyzed by Foster and
Newlon, reference above, who give a formula
••L,
bo2 V4b02 + tf
ohms
(17)
Symbols have the same meaning as for eqs. (14) and (15), p being the loss factor of the
core material. The loss factor must be determined by measurements upon a sample of
the particular core mate-
Table 3. Ring Permeability and Core-loss Coefficients rial. Published data are
not available on the loss
factor of cylindrical cores.
In Table 3, the figures
for the permalloys are
taken from Legg and
Given. Figures for the
other materials are Gen-
eral Aniline and Film Cor-
poration data, published
in the articles by H. G.
Shea, and by Beller and
Altmann, previously re-
ferred to.
PERMEABILITY
TUNING, or "variable re-
luctance tuning," is the
system of adjusting a cir-
cuit to resonance, at a de-
sired frequency, by mov-
ing an iron core in or out
of the coil. A simple ar-
rangement for doing this
is to mold a screw in one
end of a cylindrical core as illustrated in Fig. 17 (c). The screw passes through a tapped
hole in the coil housing and is slotted at the end for a screwdriver. Rotation of the screw
moves the core axially into or out of the coil, varying its inductance and the resonant
frequency of the circuit. Such a system is ideal for a circuit tuned to some fixed frequency,
such as an intermediate-frequency transformer circuit. See "Ferro-inductors and Perme-
ability Tuning," W. J. Polydoroff, Proc. I.R.E., May 1933.
Incremental permeability tuning is a system of adjusting the resonant frequency of a
circuit by varying the permeability of the iron core without any mechanical motion. The
permeability is varied by means of d-c magnetization on the same principle as the saturable
reactor. Increase of d-c magnetization causes a decrease of inductance and an increase
of frequency. By proper design, the increase of frequency, from some minimum value,
may be made proportional to the direct current. "Incremental Permeability Tuning,"
W. J. Polydoroff, Radio, October 1944.
Material
Perme-
ability
Hysteresis
t*a X 103
Residual
MC X 103
Eddy
Current
IJ.6 X 106
2-8 1 Molyb. Perm
2-81 Molyb. Perm
2-81 Molyb. Perm
8 1 Permalloy
125
26
14
75
0.20
0.18
0.16
0 41
3.8
2.5
2,0
2 8
2.4
0.2
0.1
3 8
81 Permalloy
26
0.30
2.8
0 7
Carbonyl "55". .
55
0.86
18.0
0 073
Carbonyl L
39
1.45
27.0
0. 10
Carbonyl L
24 8
3 1
0 13
Carbonyl C
16 7
1 i
0 14
Carbonyl E
10.4
0.3
0. 11
Carbonyl TH
9.6
0.3
0. 10
Carbonyl SF
8 1
0 3
0 10
Electrolytic
23 4
2.4
0 33
Hydrogen-reduced. . .
Hydrogen-reduced. . . .
Hydrogen-reduced. . . .
Hydrogen-reduced. . . .
Magnetite
42
18.4
16.9
12.5
7 9
1.04
2.6
1.0
3.1
9. 1
23.0
0.17
0.12
0.12
0.11
11.5
Magnetite
5.7
6.8
0.21
Magnetite
3.1
0.3
0.085
CLASSIFICATION OF CAPACITOKS
3-53
CAPACITORS
By James I. Cornell
A capacitor or condenser is an electrical device used primarily because it possesses the
property of capacitance. Though capacitor is the preferred engineering terminology, the
term condenser is still widely used.
Electrostatic capacitance is denned as the ratio of the electrical charge Q stored in the
capacitor by virtue of the applied voltage (J?dc) . That is, when a d-c voltage is impressed
on two conductors insulated from each other, the voltage causes an electrical charge to
flow into the system. One conductor assumes a positive charge and the other an equal
negative charge, depending upon the polarity of the impressed voltage. The charge on
the conductors produces electrostatic stresses in the region between them. The work
done in charging the capacitor appears as stored potential energy. This energy is released
when we remove the impressed voltage and short-circuit the capacitor electrodes. The
capacitance is a measure of the charge or stored potential energy for a given voltage. In
terms of physical units, a capacitor having a capacitance of 1 farad will store 1 coulomb of
charge or 1 watt-second of energy for 1 volt of applied direct voltage.
17. CLASSIFICATION OF CAPACITORS
Capacitors may be classified according to form, dielectric medium, and electrode structure.
Generally, the classification of capacitors according to form is determined by whether
the capacitance is variable or fixed.
Variable capacitors cover two essential types, namely:
1. Variable capacitors provide for continuous control of the capacitance and are used
for varying the resonance frequency of a
tuned circuit with which it is associated.
The dielectric employed may be air, com-
pressed gas, or liquid types. See Fig. 1.
2. Adjustable capacitors provide for lim-
ited control of the capacitance, and these
capacitors are usually found in frequency-
determining circuits for alignment pur-
poses such as intermediate-frequency
transformers, etc. The dielectric medium
used in adjustable-type capacitors may
be air, mica, or some form of ceramic.
Fixed capacitors employ a wide range
of dielectric materials, and, because of the
different dielectric media used, the form
and usage of these capacitors must be
evaluated according to their dielectric in
terms of circuit requirements. The wide
variation in the kinds of dielectric mate-
rials available for capacitors permits con-
struction to meet practically all kinds of
circuit requirements.
FIXED CAPACITORS CLASSIFIED ACCORDING TO DIELECTRIC MEDIUM.
Gas Dielectrics. Vacuum and compressed-gas-filled capacitors are designed for elec-
tronic power circuits where high voltage, high current, and high frequency requirements
are encountered and where other types of dielectrics are inadequate because of excessive
losses and resultant overheating.
Impregnated Paper. The most common form of solid-dielectric capacitors employed
in electronic and communication circuits are impregnated-paper types. High-purity kraft
paper may be impregnated with micro crystalline hydrocarbon waxes, chlorinated waxes,
vegetable oil, mineral oil, Askarels or synthetic chlorinated oils, and plastics. Impreg-
nated-paper capacitors are usually made up in a multiple-layer foil and paper structure
of rolled construction and are impregnated after winding.
Plastic Film. Special design considerations such as low dielectric absorption or high
operating temperatures have resulted in the development of plastic-film dielectrics, using
such substances as polystyrene, acetate, or butyrate. These follow the general construc-
tion of the impregnated-paper types except that the plastic dielectrics are in final form and
FIG. 1. Typical Variable Capacitors
3-54 RESISTORS, INDUCTORS, CAPACITORS
are Impregnated only for the purpose of removing surface moisture and eliminating voids
in the winding.
The principal virtue of polystyrene lies in the very low absorption characteristic and its
low losses at radio frequencies. Its use is limited to an operating temperature of 85 deg
cent. Other synthetic plastic films such as acetates and butyrates have been found useful
for applications requiring operation at ambient temperatures exceeding 85 deg cent, and
they have been operated experimentally at 150 deg cent. They usually have high r-f power
factor, and their use is restricted to d-c or low voltage a-c circuits where high ambient
temperature is the principal consideration.
Inorganic Dielectrics. Common inorganic dielectric materials are solid dielectrics con-
sisting of mica, glass, and ceramic types; also liquid dielectrics such as silicone oils. The
solid dielectrics are usually in sheet or plate form which require a laminated stacked con-
struction. The electrodes may take the form of foil, or a silver coating deposited directly
on the surface of the dielectric before the stacking operation.
Ceramic dielectrics are supplied in a variety of shapes other than laminal, and one of
the most popular is a hollow cylinder with the electrodes placed on the inner and outer
surfaces in the form of a silver coating. They form a capacitor whose capacitance is a
function of the dielectric constant of the ceramic. Capacitance values are usually low or
less than 2000 n/mi. The dielectric constant and temperature coefficient of the ceramic
body can be varied widely to give capacitors with negative, positive, or zero temperature
coefficients of capacitance.
This form of capacitor is receiving more consideration in r-f circuits where a negative
temperature coefficient is used to compensate for the positive temperature coefficients of
other circuit elements with which they are associated.
The electrode structure used with a silicone oil dielectric is of the rigid grid type similar
to that found in variable capacitors. Silicone oils will withstand high ambient tempera-
tures and are characterized by low r-f power factor.
Oxide Film Dielectrics. Electrolytic capacitors owe their unusual characteristics to
the oxide film dielectric layer which is produced electrochemically on aluminum, tantalum,
and certain other metals. Details of this form of dielectric will be found under the subject
"Electrolytic Capacitors."
CLASSIFICATION OF FIXED CAPACITORS ACCORDING TO PLATE STRUC-
TURE. Rigid multiple parallel plate structure used in connection with gas or liquid di-
electrics. Under this classification may be found the silicone and compressed gas capacitors
for high-power, high-frequency radio transmitting and dielectric heating circuits; also wet
electrolytic capacitors for use in low-voltage receiver power-supply filters.
Interleaved foil or stack construction used in connection with mica, glass, ceramic, and
plastic film solid dielectrics.
Helical or Rolled Plate Construction. The most common form of plate structure for
solid dielectrics such as impregnated paper, plastic film, and electrolytic types is the helical
or rolled plate construction. In this construction the electrodes are of very thin foil
separated by a single- or multiple-ply dielectric layer and wound into a cylindrical roll.
Metallized plate construction where the electrodes are deposited on the surface of the
dielectric. This construction is used with mica, ceramic, glass, plastic, and impregnated-
paper dielectrics.
CAPACITOR CHARACTERISTICS. Variable Nature of Capacitance. Three principal
characteristics of any dielectric medium influence the physical form of capacitors:
1. Dielectric constant or specific inductive capacity, denoted by K.
2. Dielectric strength.
3. Dielectric loss or power factor.
The dielectric constant is a numerical quantity, expressed as the ratio of the capacitance
of the structure with a dielectric other than air to the capacitance with air as the dielectric.
In other words, the higher the specific inductive capacity or dielectric constant (K) , the
smaller the size for a given capacitance. Note: Refer to Section 2 for the dielectric constant
of various materials.
Dielectric strength may be defined as the property of the dielectric by which it with-
stands breakdown when a voltage is applied to it. The dielectric strength is expressed in
volts per mil of dielectric thickness. The shape of the electrodes by which the voltage is
impressed on the dielectric and the duration of the impressed voltage help to determine
the rupture voltage. When the applied voltage is alternating, the wave shape and fre-
quency of the voltage affect the dielectric strength. Because of these variables, the dielec-
tric strength in volts per mil is not a constant and is usually expressed as a voltage range.
Capacitance varies inversely as the plate separation or dielectric thickness. The limiting
minimum, thickness is the voltage that the capacitor is required to withstand. Therefore,
the higher the dielectric strength, or breakdown potential, of the insulating medium, the
VARIABLE AND ADJUSTABLE CAPACITORS 3-55
thinner the dielectric and the larger the capacitance value for a given electrode area. This
can best be illustrated by comparing ceramic dielectric to the oxide film dielectrics of
electrolytic capacitors. Most ceramic dielectrics are limited to a breakdown potential of
less than 100 volts per mil, whereas the oxide film thickness of an electrolytic capacitor is
measured in microns and will withstand a voltage stress equivalent to a million volts per
mil of dielectric thickness.
D-c Leakage. Continued polarization of a capacitor by direct voltage after full electri-
fication results in a flow of current termed the leakage current. Though the d-c leakage
is negligible under most conditions of operation, it varies with temperature and should be
taken into account in circuit designs, especially those involving grid coupling capacitors
or similar circuits which are affected by the flow of conduction current in the capacitor.
Dielectric Polarization and Absorption. Capacitors with solid dielectrics take longer to
charge than would be predicted from their theoretical constants, owing to a lag or delay
in polarizing the dielectric medium. This is known as dielectric polarization. When a
capacitor is discharged by short circuiting, all its energy is not released and it will build up
a new charge with time which is known as the residual effect. This characteristic is known
as dielectric absorption. Both are detrimental to circuits requiring rapid charge and dis-
charge characteristics. Selection of a dielectric like polysty- _
rene is dictated in circuits where dielectric absorption must be "
held to the absolute minimum.
Figure 2 illustrates schematically what takes place in a ca-
pacitor having d-c leakage and dielectric absorption. C repre-
sents the geometric capacitance based on a perfect dielectric.
Ci and n represent the absorption effect. The pure conduction FlG' 2' cSJSS^Cireuit °
effect is represented by r*
Power Factor, Q, or A-c Resistance. When a capacitor is operated under a-c voltage
stresses, the dielectric will heat up, depending upon the frequency of the applied voltage.
The a-c resistance or the power factor is a measure of the heat dissipated. It is more con-
venient in working with electrical circuits to use a ratio of the pure reactance to the
effective resistance which is termed the Q factor. The Q factor can be employed for the
purpose of comparing various capacitors quantitatively since it constitutes a figure of
merit for a given design.
It is easily seen that, although so-called fixed capacitors may be made up using any
one of the many different types of dielectrics, the actual capacitance is a variable depend-
ing upon the physical characteristics of the dielectric, which vary with:
A. Voltage, Capacitance will change with voltage. The voltage coefficient will vary
with the magnitude of the d-c or a-c impressed voltages.
B. Frequency. The capacitance will change with frequency and is a function of the Q
or power factor of the dielectric.
C. Time. Capacitance will change with time because of dielectric aging.
D. Temperature. Capacitance values will change with temperature since dielectrics
change with temperature or have a temperature coefficient.
These characteristics serve to demonstrate the fallacy of considering a capacitor as an ideal
fixed capacitance.
Inductance. In addition to the limitations imposed by the dielectric media, another
limitation, which results from mechanical design, is inductance. All capacitors have a
self-resonant frequency and behave like a circuit involving series inductance, resistance,
and capacitance. Above the critical frequency, the reactance is inductive and not capaci-
tive. In fact, capacitors behave like a complex impedance depending upon the operating
frequency range.
18. VARIABLE AND ADJUSTABLE CAPACITORS
Capacitors designed for frequent adjustment by an equipment operator are usually
termed variable or tuning capacitors. Capacitors of this type most often use an air di-
electric, although other dielectrics are suitable for special circumstances. For example,
compressed air or nitrogen dielectrics reduce the size of high-voltage capacitors in large
transmitters. Mineral oil, silicone fluid, and other liquid dielectrics save space because
of their higher dielectric constant. In addition, such capacitors have a higher breakdown
voltage for the same interelectrode spacing.
Capacitance adjustment in variable capacitors is usually made by varying the effective
plate area. The capacitor consists of two sets of parallel intermeshed plates, one fixed
and one rotatable on a mounting shaft. Rigidity of the capacitor framework and freedom
from warpage of the plates and the stator insulation are extremely important from the
3-56
RESISTORS, INDUCTORS, CAPACITORS
standpoint of circuit stability. For extremely stable circuits in high-grade electronic equip-
ment, carefully designed Invar steel frames and plates may be used to minimize capacitance
shifts with ambient temperatures. More commonly frames and plates are of aluminum
or silver-plated brass. In the cheapest broadcast receivers, cadmium-plated steel has been
used. To facilitate tracking of circuits in broadcast receivers, the outer rotor plates are
sometimes slotted to permit small adjustments in the capacitance-rotation curve. The
supporting insulation for the capacitor stator is usually phenolic or ceramic, depending
upon circuit considerations. Electrically low-loss, dimensionally stable steatite or glass-
bonded mica insulation is used in capacitors where high Q and low capacitance drift are
important. In the highest grade of precision laboratory standard capacitors the insulation
is quartz.
In certain highly accurate instruments, the "standard" variable capacitors consist of
two co-axial cylinders, one fixed and one movable.
Capacitors intended for relatively infrequent adjustment of capacitance are termed
"trimmer or adjustable" capacitors. Most common in broadcast receivers is the small mica
trimmer capacitor. Such a capacitor consists of a fixed and a hinged movable metal
electrode mounted on a phenolic or ceramic base with a mica spacer between the two elec-
trodes. The movable leaf is raised or lowered by threading it on a screw. These capacitors
are sometimes called "book mica trimmers."
In high-grade electronic equipment, especially for frequencies above the standard broad-
cast band, trimmer capacitors similar in construction to intermeshed plate variable capaci-
tors are used. In many cases, they have a shaft positioning locking device such as a
split tapered bushing and nut. Also found in such equipment are adjustable ceramic
capacitors. These capacitors consist of two coaxial half-silvered ceramic disks, one fixed
and one rotable. The ground unsilvered faces are kept in contact by spring pressure.
The capacitance depends on the extent of overlap of the silvered faces. Through selection
of various ceramic compositions an opportunity is provided for some degree of circuit
temperature compensation.
Transmitter neutralizing capacitors are a special design of adjustable capacitors consist-
ing of a fixed disk with rounded edges and a similar coaxial movable disk mounted on the
end of a set screw. Capacitance adjustment is by turning the screw in and out of a
threaded support.
In high-powered aircraft transmitters, adjustable vacuum capacitors are sometimes
employed. These capacitors have a metal bellows to permit positioning the movable
capacitor element.
The maximum capacitance of variable capacitors usually employed in electronic circuits
is from 10 to 530 jujuf . For use as a capacitance standard, units are made with capacitances
up to 5000 npf. Trimmer capacitors may have a maximum capacitance of 5 to 75 pid-
Since air dielectric capacitors have very little loss in the dielectric and supporting
insulation, they will show practically no change in capacitance with frequency. Accurate
measurements of capacitance values at audio frequencies may therefore be depended upon
at radio frequencies with a good degree of precision.
EFFECT OF STRAY CAPACITANCE. Units of variable capacitance generally are
for relatively small values, and in a circuit, particularly at high frequencies, the capacitance
effects of the various other parts of a circuit will be appreciable as compared with the
capacitor unit. Every part of the apparatus has capacitance to other parts, and these
small stray capacitances may be appreciable. The stray capacitances are particularly
objectionable because they vary when parts of the circuit or conductors near by are moved,
such as the hand or body of the operator. The disturbing effects may be minimized in
practice as follows: (1) by keeping the capacitor a considerable distance away from con-
ducting or dielectric masses; (2) by shielding the capacitor, that is, surrounding the whole
capacitor by a metal covering connected to
one of the sets of plates; (3) by using a capaci-
tor of sufficiently large capacitance so that
stray capacitances are negligible in compari-
son. The first two of these methods reduce
only the stray capacitances of the capacitor
itself to other parts of the circuit and to ex-
ternal moving bodies. Although the third
procedure is workable for the lower radio fre-
quencies, it fails at the very high and ultra-
high frequencies, and an entirely different
approach to the problem has been necessary.
Karplus has described a variable capacitor design which includes the circuit inductance.
In this design, wide tuning range with simultaneous change of lumped capacitance and
FIG. 3. Semi-butterfly Circuit
VARIABLE AND ADJUSTABLE CAPACITORS 3-57
inductance is obtained by rotation of a member that does not require any electrical con-
nections. This arrangement is called the butterfly or semi-butterfly circuit, depending
upon the configuration of the variable capacitor design. Figure 3 shows such a circuit.
Maximum and minimum capacitance of a butterfly circuit can be computed as in a
variable air capacitor, but, owing to the butterfly shape, capacitance ratios are considerably
less than in well-designed tuning capacitors.
CAPACITANCE FORMULA. The general expression for the capacitance of a multi-
plate capacitor is (in micro-microfarads)
C = 0.08852S: (Ar~ 1)S (1)
in which S is the area in square centimeters of a moving plate overlapping a fixed plate;
T is the separation of plates in centimeters; K is the dielectric constant (for the air capaci-
tor, K = 1) ; JV is the total number of similar plates (fixed plus movable) , alternate plates
being connected in parallel. In eq. (1) no correction is made for the curving of the lines
of force at the edges of the plates; this effect is negligible for most capacitors, when T is
very small compared with S.
The numerous applications of variable capacitors in radio circuits place different require-
ments upon the capacitor in its characteristic variation with setting. For laboratory use a
capacitor is usually designed with semicircular plates. With this form the capacitance
increases linearly with the angular displacement of the movable plates. In other radio-
circuit applications it is convenient to have the capacitance vary with the setting to some
other power than the first, and these forms are noted below.
Plate Form, Semicircular. In a variable capacitor of the semicircular type the effective
area of the plates is changed by rotating the movable plates. Throughout the entire plate
rotation the capacitance is proportional to the setting, provided that the capacitor is well
constructed and the distance between the two sets of plates is not affected by rotation of
the movable set. When the plates are entirely unmeshed (no overlap), measurement
usually will show that there is an appreciable capacitance between the capacitor terminals.
For a 5000-/zMf capacitor this may be as large as 75 jujuf . This value is practically unaffected
by the position of the movable plates on the rotor, and it represents the capacitance be-
tween the insulated binding posts and the small capacitance formed across the insulators
which separate the plates. The capacitance of a variable capacitor cannot, therefore,
be reduced to zero, and such relations as are developed for capacitance-rotor positions hold
only when the plates are enmeshed a considerable amount. Throughout the range in
which the capacitance curve is linear the capacitance is given by the expression
C = ad •+• Z>, in which 6 is the angle of rotation of one set of plates with respect to the other.
Plate Form, Logarithmic. In a special form of wavemeter, called the decremeter, the
plates are so formed as to determine the logarithmic decrement of a circuit. This is meas-
ured by the percentage change in capacitance required to reduce by a certain amount the
indication of an instrument in the circuit at resonance. In order that equal angular rota-
tions may correspond to the same decrement at any setting of the capacitor, it is necessary
that the percentage change in capacitance for a given rotation shall be the same at all
parts of the scale. In order that each degree displacement give the same percentage
increase in capacitance the following requirement must be satisfied:
^ = adO (2)
where a = constant = percentage change of capacitance per scale division. Integrating,
log C - ad 4- 6 (3)
where 5 = a constant
C = ««*+&> = Coe06 (4)
where Co = eb = capacitance when 9 = 0.
Since the area must vary as the capacitance:
A - 1/2 /> dd == Coe06 (5)
using polar coordinates
and _ .
r = V2CQaea6 (7)
The last expression is the polar equation of the bounding curve required to give a uniform
decrement scale.
3-58
RESISTORS, INDUCTORS, CAPACITORS
Plate Form, Wavelength. For certain applications it is desirable to have the wave-
lengths proportional to the setting of the capacitor. Since the wavelength varies as the
square root of the capacitance, this will require that the capacitor plates be formed so
that the capacitance of the circuit varies with the square of the setting. In designing the
shape of these plates, allowance should be made for the stray capacitance of the circuit.
For the design of the simple straight-line wavelength capacitor the following expressions
axe used: /0,
C = A = ae2 (8)
In polar coordinates the area
A - V2 V dd
(9)
Differentiating both expressions:
(10)
which is the polar equation of the bounding curve to give the desired characteristic.
Plate Form, Frequency. In another type of capacitor, of much more importance than
those mentioned above, the variation of capacitor setting is directly proportional to the
frequency for which the total circuit is tuning. The importance of this type follows from
certain considerations in radio communication, which require the spacing of broadcasting
stations from each other by equal increments in frequency. It is this condition which
makes highly desirable a capacitor so designed that equal increments in capacitor setting
advance by equal increments the frequency to which the associated circuit is tuned.
Such a capacitor will tune for the various broadcasting stations at equally spaced points
in the capacitor dial.
In making this special form of variable capacitor the shapes of either rotor or stator
plates may be adapted to perform the required area-setting variation. It is usually more
convenient to use ordinary semicircular stator plates and form the rotor plates to the
required shape. On this basis Forbes has shown that the radius vector to the edge of the
rotor plate must satisfy the relation:
(ID
in which D = l/(2irVL); L = inductance of the circuit in henries; n = number of di-
electric spaces; fc = lQ-ll/(36ird) ; d = length of air gap between plates; K = (/o° - /iso0)/*-
= cycles per radian of capacitor scale; /o°
= frequency of circuit with capacitor set at
0 deg; /iso0 = frequency of circuit with
capacitor set at 180 deg; Co = total capaci-
tance of circuit when capacitor is set at 0
cleg — this includes stray circuit capacitance
as well as that of the zero setting of the ca-
pacitor in farads; 9 = angle of rotation of
the plates, radians; and n = radius of the
cut-out of stator plates to accommodate the
rotor shaft. All dimensions in centimeters.
The capacitance of such a capacitor, for any
angular position 6 of the rotor, is
D
500
f
1 400
£
20°
40 60 80
Sea e Reading. Divisions
100
100 _ _
'~ (12)
Typical variations of capacitance with
setting are shown in Fig. 4, which represents
FIG. 4. Capacitance Calibrations for Three Typi- the construction practice of one manufac-
^^/iS^^^rSl!1^! turer of variable capacitors. The curves
Straight-line Frequency shown indicate the value of capacitance ob-
tained for various settings of the three
general types of capacitors, straight-line capacitance (SLC), straight-line wavelength
{&LW), and straight-line frequency (SLF).
VARIABLE AND ADJUSTABLE CAPACITORS
3-59
Plate Form, Special Designs. Special considerations must be given to the design of
variable air condensers when two or more units are connected together for operation on a
common shaft. This grouping of sections into "gangs" sometimes places five condensers
on a single control, and these may perform important functions in as many individual
circuits. An illustration of this construction occurs in a radio receiver in which there are
two identical units for tuning signal frequency circuits, one unit with specially shaped
plates to tune the oscillator circuit and two smaller units to tune the short-wave circuits.
In order to integrate the actions of all these condensers in the above superheterodyne
radio receiver, where the single control is particularly desirable, various methods of design
have been developed. E. D. Koepping has described the general principles involved,
D. F. McNamee has presented a graphical solution of the design problem, and H. Schwartz-
mann has shown an analytical solution of the problem (see Bibliography, p, 3-73).
PLATE SPACING OF AIR CAPACITORS. Between two oppositely charged paraUel
plates of infinite extent the field is uniform. It is known, however, that the field between
two finite plates is not uniform, tending to greater voltage gradients at the edges. Stress
at a point in a dielectric is determined by the gradient at that point, and stresses above
certain critical values lead to the formation of corona and sparkover. This may be pictured
as follows, with plate spacing = /S and thickness as T. For large values of S/T, the radius
of the plate edge is small and a high gradient exists. As the plate thickness is increased,
keeping plate center-to-center spacing and applied voltage constant, the radius of edge
curvature is increased. This decreases the edge gradient. Inside the capacitor, however,
the gradient increases because of the reduced spacing. It has been suggested by Ekstrand
that the best value of S/T may be between 2 and 3. Investigation seems to corroborate
Ekstrand figures by fixing the optimum S/T at 2.77.
Plate Dimensions and Voltages of Capacitors at Various Frequencies
T
in.
S
in.
S/T
Sparkover Voltage
Maximum Gradient
kv
© 60 cy.
kv
© 700 kc
kv
© 1500 kc
kv/in.
@ 60 cy.
kv/in.
@ 700 kc
kv/in.
© 1500 kc
0.128
0.04
0.064
0.218
0.192
0.719
1.705
4.8
11.24
14
8.4
24
13.5
7.59
14.28
13.7
6.82
11.7
89.1
80.2
82.0
85.8
72.5
48.8
87.1
75.1
40.0
It has become a habit to consider breakdown as coincidental with sparkover. Actually,
breakdown has occurred at the first sign of corona, and corona may become evident at a
considerably lower voltage than sparkover. When a conductor is raised beyond a certain
critical potential, 'the air adjacent to it becomes ionized, forming corona. The ionized air,
2000
4000
6500
^ 9000
£13,000
<u
216,000
Sea level
30
28
26
22 1
16 g
14 1
1
12 o
10 1
s
8i
6
4
1
/
/
—
1
/
X
—
j
/
x
X
—
«?/
tf
r
x
<
y
o
|/
°^
p
If
^
x
x
•^
/
/
/
X
0
&$$
x
X
/
/
A
x
s
<y\ 9
^x|
•^
—
I
f
/
/
x
X
^x
0
^^
.
-^
2000
15,000
31,000
38,000
50,000
3C
/
/
'
/
^
^x
x
^x
-^o
£ga
i
/
t
/
/
X
/
^
^
^
x^
.^
^
/
/
/
X^
^
^x1
x^
^f
*^
—
/
/
/
x
^>,
^
x-^
^*^"
_
/
x
x
-"^
^?
^
*^
_^
X
^
r^
)0 500 700 900 1100 1300 1500 1700 1SOO 2100 2300
D-c breakdown voltage
FIG. 5. Breakdown Voltage vs Altitude (Atmospheric Pressure)
3-60
RESISTORS, INDUCTORS, CAPACITORS
being itself a conductor, can be considered to increase the dielectric losses. If the gradient
is further increased, the conditions become unstable and sparkover occurs.
Not only are capacitors used in transmitters and electronic heating devices subjected to
high voltages, but they also must carry considerable amounts of power. The power input
to a capacitor is measured by the energy stored in it multiplied by the number of charges
and discharges per second.
Transmitter capacitors used in aircraft electronic equipment must have their plates
spaced properly to withstand voltages encountered at maximum flying altitudes. The
curves of Fig. 5 indicate breakdown voltage for various plate spacings at various altitudes.
19. IMPREGNATED-PAPER CAPACITORS
Impregnated-paper capacitors are the most efficient of all types because of their
flexibility in size, shape, and rating. They cover an extremely wide range in size from the
small toothpick varieties found in hearing aids to large welded case blocks. Flexibility
in voltage ratings is second only to size values with a range from 1 volt to 200,000 volts.
Capacitance values are common in a range from lOOju/xf to 200^f in a single container.
Electronic equipment designers are primarily concerned with d-c application of impreg-
nated-paper capacitors.
D-c service includes such applications as rectifier niters, energy storage, arc suppression,
and by-passing for electron-tube and circuit elements. D-c ratings provide for small a-c
components where their heating effects are negligible. Experience indicates that the a-c
Edges of foil sweflged
both ends
Thined copper tabs
Inductive and Non-inductive Capacitor Windings
components should not exceed 20 per cent of the d-c value at a frequency of 60 cycles, or
15 per cent for 120 cycles, or 1 per cent for 10,000 cycles, and for higher frequencies the
allowable magnitude is determined strictly on thermal evaluation of the high frequency
component.
Other special electronic applications require rating of the capacitor on an a-c rather than
a d-c basis, such as tuned niters and pulse networks.
A-c versus D-c Ratings. It is possible to rate capacitors designed for a-c service in
terms of d-c voltages, but it is not practical to rate d-c capacitors in terms of a-c voltage
ratings because of the difference in design considerations in the d-c rated capacitors in
comparison to those rated for alternating current.
Some of these design considerations are:
1. D-c voltage ratings depend essentially on dielectric stress.
2. A-c voltage ratings depend not only on dielectric stress but also on the operating
frequency and power factor. Frequency and power factor determine the internal heating,
which must be kept within limits determined by the radiating surface of the container.
For small a-c capacitors, the ratings are determined from dielectric breakdown voltage
considerations. In the larger a-c voltage ratings, the prime design consideration is heating.
In general, the following tabulation represents the nearest standard d-c rating corre-
sponding to the several standard a-c voltage ratings:
A-c VOLTS
110
220
330
440
550
660
D-c VOLTS
200
400
600
1000
1500
2000
Chlorinated diphenyl impregnated capacitors designed for a-c service cannot be used
on direct current unless the impregnant has been chemically treated with inhibitors or
IMPREGNATED-PAPER CAPACITORS
3-61
stabilizers to prevent deterioration of the impregnant from the combined influence of the
d-c field and high temperature.
Construction of Winding. Impregnated-paper capacitors are made in a roll construc-
tion, consisting of two metallic foils separated by two or more sheets of impregnated kraf t
tissue. In the roll construction the resultant capacitance is twice that obtained with a
parallel-plate construction since both sides of
the foils are active. The capacitor winding
may be round or flat, depending upon mechani-
cal considerations of housing.
A further consideration in roll construction
is whether the foils are of the "buried" type
with tabs for contact members or of the ex-
tended foil construction. See Fig. 6(a) and (6).
The extended foil construction gives the low-
est value of self-inductance since all the turns
are bonded together, the construction ap-
proaching that of a stacked parallel-plate
capacitor. The "buried" foil winding ap-
proaches the "extended" foil if the tabs are
inserted at the center of the winding within
one turn of each other. Figure 7 shows a com-
parison of the impedance for "extended" vs.
"buried" foil constructions for a frequency
range of 60-5000 cycles.
Impregnation of Winding. The impregnants most commonly used with kraft paper
are microcrystalline hydrocarbon waxes, chlorinated waxes and oils, castor oil, mineral
oil, and plastic compounds. These various impregnants offer a wide range of characteristics
with temperature. Figure 8 shows six of the more common wax and oil impregnants for a
temperature range of —40 to 100 deg cent. These data were taken for average production
capacitors and do not represent minimum requirements. Minimum requirements are
shown in the accompanying Table 1.
Voltage Rating of D-c Capacitors with Temperature and Service Conditions. All
capacitors are affected by temperature, voltage stress, and time.
Table 1. Minimum Impregnant Requirements
Power factor tn per ceTjt
i-» »-« M M OJ O> -N -1
010 01 O 01 o 01 o tri oc
/
/
/
Inductive, tat!
center of wir
s fn
ding j
/
A
In
e
du
nc
"ctve, tabs at
of windings^/
/
\
^^
\
^
***•
***
***
"•
.—--
•inductiv
~*^
e win
ding
— " Non
)0 1000 2000 3000 50C
Frequency In cycJes
FIG. 7. f Comparative Power Factors for Induc-
tive and Non-inductive Windings
Castor
Oil
Mineral
Oil
Chlorinated
Diphenyl
Halowax
Megohms times microfarads:
At 25° C
500
2000
1500
2000
At high test temperature *
5
20
15
100
Insulation resistance in megohms:
At 25° C
1500
6000
4500
6000
At high test temperature . •
150
600
450
1000
Capacitance change in per cent at low ambient test
temperature from value at 25° C t
-30
-15
-30
-10
* 85° C for all impregnants except Halowax, which is measured at 65° C.
f Lowest temperature —40° C except for Halowax, which is —20° C.
It has been standard practice to rate d-c capacitors at a 40 deg cent ambient temperature
on the basis that such a rating would provide sufficient factor of safety to withstand a life
test of 1000 hours at twice the rated voltage at this temperature, which is equivalent to
approximately 1 year of normal service conditions.
Design trends for electronic equipment toward smaller and smaller physical volume have
resulted in ambient temperatures considerably in excess of the 40 deg cent value considered
standard before World War II.
It has not been generally understood that increasing the ambient temperature above
40 deg cent required voltage derating for an equivalent life expectancy at the higher tem-
peratures, and that the derating factors are a function of capacitor size. Capacitor size
can best be evaluated for d-c ratings in terms of energy content in watt-seconds.
Watt-second = */2 CE2
where C = capacitance in microfarads and E — d-c voltage in Mlovolts.
This was a problem given joint industry and government appraisal during the war, and
the findings resulted in a table of derating factors as a function of temperature and capaci-
3-62 RESISTORS, INDUCTORS, CAPACITORS
| 1 — h-
^M^
* ?|
N
v~
=50,
noc
=4^
}3
1 '
"N-
"3
N
-2
?'C
00
r
\
10,000 -S
1
vv
5,000 |«5
1
2,000'|^
\
7
Mi
ier£
1 0
i
\
1,000 1 1
fnj=
V
S
o
2
00-
50
\J
°1
&
100
—
1
9^
Sn
-—
Q. Q
I"*TH
'1. In ! ' j
|-l-2
1-2
8-4
•50,00
-+—F
2,000
10,000 rt
5,000 11
S-g
1,000 gx
500
200
ng
So
tfl-rs-
«4-2
^o 0
S-2
g ^
•^^
— «
^
«5^
Insulation resistance «-»
Megohms X microfarads
^
"""v.
^—4
ro
p.
o
S
o
a
S
IB
*c 2
1
-— -
M,!C
lydr
roc
oc<
••^i
7bq
^
a!ltn€
n wa
u
10,00
^
5,000
N
N
2,(
1,C
50
20
10
300
)00
0
0
0
S
^
==5
=1
^-40 -20 0 -t-20 +25+40 +60 -1-80 +100
Temperature in degrees caniigrade
S, +2
| o
-1—
|-10
8-14
1
1
o c
«5
c2
F
^
ss'
0,(
00
10
,00
ion resistance ^
5 X microfarads
Cas
tor
5,000
oil
2,C
l.C
)00
00
0
3
^
50
20
Oy?
3 0
«M
\.
\
s
=
s^
-1C
50
/
"1
c^-
-^~
i r--
>^
S.+4
Per cent capacitance cb
>er cent power factor - 1000 oo , , ,
oi-»tow o>itoo
"i n
00-
!— '
H
DlU
lin
itec
nib'
1 Wt,
tor
0,
)OC
1C
5,C
I/
50
20
10
,00
)00
)00
)00
0
0
0
ation resistance o
ms X microfarads
<
s,
^
\
s
il
S
— ».
**^
•H —
1-4°
S 8
(^
Insulation resistance o
Megohms X microfarads
/*
sr*
p,boc
r~ 2
\
o,c
00
10,00
"5_ifi
— /
ite<
tnh
\
1 d p
ibito
Percentcapa
ower factor - 60 ^ T I i
oo 4, a. gg^{
y
^
irin
JlUS
_^
/
Jhlc
I
henyl
r
S
5,C
2,C
1,C
50
\
)00
>00
00
0
\
\
*
K
0-
)0-
^
R
/
-2
-/L
^
Si
MM"
^
-i
=>- =
^z=
*•**
=±:
-40 -20 0 +20+25+40 +60 +80 +100
Temperalore in degrees centigrade
Typical Electrical vs Temperature Characteristics of Paper-dielectric Capacitors with. Various
Impregnations (Courtesy of Solar Mfg. Corp.)
IMPREGNATED-PAPER CAPACITORS
3-63
tor size. These data are shown in Fig. 9 and are extracted from data obtained in Proposed
Joint Army-Navy Specification JAN-C-25 dated January 22, 1945, and published in
Communications for August 1947.
These data show that a capacitor in the 0.5 watt-second class and rated for a given
voltage at 40 deg cent must be voltage-derated to 95 per cent of its 40 deg cent rating at
85 deg cent or 60 per cent at 105 deg cent. Generally speaking, the life expectancy of a
Capacitance Rated Watt -
/Xf A-W-S volts sec
Permissible volts
-Per cent at-
o.oi-
-103 |
55 C
65 C
75 C
850
Q.
0.02-
-203
-100,000
-100 o
-75,000
I °
— 50 000
,,
85
80
65
45
0.05-
-503
-40,000
-40.0^
-30,000
-30.0
-25,000
o.i-
=104
-20,000
"20.0^
-15,000
g
-12,500
0
0.25~
"254
-10,000
-10.0
-7,500
-6,000
— c QQQ
90
85
70
55
0.50-
-504
-4,000
-4,0
-3,000
-3.0
-2,500
1.0Z
=105
-2,000 ^^
-2.0 ~
-1,500 ^.^"^
1
2,0-
-205 ^>
^Cooo
Z1.0
A. r\
"^--^^
-600
95
85
75
65
4.0*
•*"405
-400
-0.4
6.0-
-605
-0^
8.0-
-805
-250
10.0-
:106
-200
-0.2
12.0-
-126
15.0-
-156
T-l
20.0-
-206
-100
= °'10 |
30.0-
-306
~ <5
40.0-
-406
-0.05
50.0-
-506
95
90
80
70
100-
FIG. 9. Ratings of D-c Capacitors
capacitor without derating is halved for each 10 deg cent rise in temperature. For d-c
voltage considerations, at a fixed temperature of 40 deg cent, the life expectancy is in-
versely proportional to the fifth power of the voltage.
D-c voltage ratings are not fixed values, but for a given insulation thickness they may-
be made variable depending upon the duty cycle and circuit conditions. A capacitor rated
at 1000 volts d-c at 40 deg cent for continuous duty in a power-supply filter could be used
in a photoflash circuit at a much higher voltage, such as 2000 volts d-c, and still have
acceptable performance because of the lighter duty cycle. Life expectancy might increase
to 100,000 flashes of the photoflash equipment.
This indicates that considerable flexibility may be used in rating capacitors provided
that all the design requirements, operating conditions, and duty cycle are known. To
illustrate, a 10-^f capacitor winding using three sheets of 0.0004 kraft tissue and impreg-
nated in mineral oil would be normally rated at 1000 volts d-c at 40 deg cent continuous
duty, at 1200 volts for an intermittent duty cycle of about 50 per cent, at 1500 volts inter-
mittent duty for welder applications, and 2000 volts under a photoflash duty cycle. The
d-c rating would have to be reduced to 600 volts for long-time (15 years) life expectancy.
Factors that affect capacitor ratings:
1. Microfarad value and tolerance.
2. Duty cycle, continuous or intermittent.
3-64 RESISTORS, INDUCTORS, CAPACITORS
3. Ambient temperature range.
4. Ripple voltage, magnitude, and frequency.
5. Abnormal circuit voltages, such as no load voltage and peak charging voltage.
6. Discharge current, and nature of discharge, whether oscillatory, and, if so, whether
critically damped.
It is well to remember that these factors that govern ratings are based on hermetically
sealed capacitors which have been carefully dried, impregnated, and sealed. They do not
apply to other constructions where life is limited by the vagaries introduced by moisture
absorption.
METALLIZED PAPER CAPACITORS. The latest addition to the family of impreg-
nated-paper capacitors is the MP type, in which the capacitor electrodes are deposited
on the paper dielectric in very thin films, having a thickness range between 25 and 100
millimicrons. The thin film contributes the property of "self-healing" to capacitors, per-
mitting the use of a single sheet of dielectric, which is not possible with conventional im-
pregnated kraft paper designs. The combination of the extremely thin metallic film elec-
trode and a single sheet of dielectric affords extremely compact designs for voltage ratings
below 200 volts d-c or for 150 volts a-c.
Voltage ratings exceeding 200 volts employ a multiple-layer or interleaved paper di-
electric of conventional construction. The volume saving is not as great as for the single-
layer construction but is still considerable.
A new concept in capacitor rating is involved with MP capacitors, namely sparking
voltage; this is defined as the lowest applied voltage
Table 2. D-c Voltage Ratings that ^ cause continuous "self-healing" action to
take place.
D-c Working
Voltage
25° C
200
400
600
1 Minute
Flash Test
25° C
300
600
900
Sparking
Voltage
25° C
400
900
1350
MP capacitors designed so that the maximum
surge voltage encountered in service at the highest
operating temperature does not exceed the sparking
voltage are usable in all kinds of circuits without
fear of their causing spurious noise. In the event
of a transient voltage which would cause failure of
a conventional capacitor type, there will be only a
momentary arc discharge followed by the self-healing mechanism.
Insulation Resistance. The minimum insulation resistance of single-layer lacquered
metallized paper capacitors will exceed 500 megohm microfarads or 2000 megohms at 25
deg cent. Interleaved unlacquered metallized paper capacitors will have a minimum
insulation resistance of 1000 megohm microfarads or 6000 megohms at 25 deg cent, which
compares favorably with conventional capacitor designs. The change in insulation resist-
ance with temperature in metallised paper capacitors is similar to that of conventional
mineral oil impregnated kraft paper designs, or there is approximately a 50 per cent de-
crease in insulation resistance for every 10 deg cent rise above 25 deg cent.
Commercial Specification References.
Joint Army-Navy Specification JAN-C-25, Capacitors, Direct Current, Paper Dielectric, Fixed
(Hermetically Sealed in Metallic Cases) .
Joint Army-Navy Specification JAN-C-91, Capacitors, Paper Dielectric, Fixed (Non-magnetic Cases).
RMA Standards Proposal 159.
20, MICA CAPACITORS
Mica capacitors are useful in electronic circuits because of their low a-c losses and their
high electrical stability over a wide temperature range. These characteristics, along with
the fact that they are constructed to very close capacitance tolerances, make them ideally
suited for use in frequency-determining circuits.
The word "mica" is derived from the Latin "micare" meaning to sparkle. It is a group
name for a number of aluminum silicate minerals which are characterized by the properties
of high reflection and a basal cleavage so perfect that they may be split in laminae of the
order of 0.0005 in. thick.
Of the eight distinct species of mica recognized by mineralogists, muscovite is the most
important as far as mica capacitor manufacture is concerned. Muscovite is virtually
unaffected by weathering, is not porous, is not decomposed by acids, and is negligibly
affected by moisture. It will withstand relatively high voltage gradients. Voltage tests
made with spherical electrodes show that films 1/iooo in. thick frequently withstand 5000
volts d-c with no puncture. Muscovite, because of its extremely low power factor, in
addition to its other desirable properties described previously, is an ideal dielectric for use
in capacitor manufacture.
Both micas and foils or silvered electrode patterns must be precision outlined. Micas
Style 20 Style 25
'
Style 56 Style 60 ®tyl8 Sioos
_ *B.OOJ _ P«0.14^0>000
2.375
.O
All dimensions in inches °-150 min'
Style 65
••l-fj-max. >
ffi~nrj
10 32 thread .
All dimensions in inches °-180 min
Style 70
All dimensions in inches \T-JI
-rdia
Style 75
When spark gap Js used
,— capacitor will be this shape
«* «"
All dimensions in Inches \T-O
Style 80
When spark gap Is used
capacitor will be this shape
All dimensfons in inches
Style 85 •
When spark gap 5s used
\capacitor will be this shape
^f
All dimensions in inches
Style 90
. When spark gap Is used
10± ie ^capacitor will be this shape
4** | H*^
All dimensions in inches
Style 95
FIG. 10. Standard Outline Dimensions
3-65
3-66
RESISTORS, INDUCTORS, CAPACITORS
for
are usually cut to within plus or minus 0.001 in. of specified lengths and widths and foils
almost as accurately.
Sealing binders as well as metal clamps provide permanent positioning of the mica stack.
This accuracy and permanency provide the sta-
bility of characteristics with respect to aging, fre-
quency, and temperature which recommend mica
capacitors for use in frequency-determining circuits
or circuits that control reactance and phase and in
precision measuring equipment.
Table 4. B-c Voltage or Peak "Working Voltage
Ratings for the Several Case Types
Table 3. Capacitance Range
the Several Case Types
Case Type
Prom
To
20
5 wrf
1 , 000 md
25
5
1,500
30
470
10,000
35
3,300
10,000
40
100
10,000
45
17
10,000
50
2,000
27,000
55 and 56
22
30,000
60 and 61
100
47,000
65
47
100,000
70
47
100,000
75
47
100,000
80
47
100,000
85
47
100,000
90
100
100,000
95
100
10,000
Note: Capacitance values for 1000 ntf
or less are measured at or referred to
500 kc/sec. Capacitance values greater
than 1000 prf are measured at or referred
to 1000 kc/sec.
Standard commercial tolerance for
Style
Voltage Range
20, 25, 30, 35
300 and 500 volts
40
300, 500, 1000
45, 50, 55, 56, 60, 61
600, 1200, 2500
65
250, 500, 1000, 1500, 2000,
3000
70
500, 1000, 1500, 2000,3000
5000
75
1000, 1500, 2000, 3000,
4000,
6000
80
1500, 2000, 3000, 4000,
5000,
6000, 8000, 10,000
90
3000, 4000, 5000, 6000,
8000,
10,000, 12,000, 15,000,
20,-
000
95
15,000, 20,000, 25,000,30
,000,
35,000
Mica dielectric capacitors because of their low
other tolerances are available as shown in
jrjg> 10.
for high current circuits.
The mechanical forms of mica dielectric capacitors
vary from small phenolic molded cases for receiver
applications to large ceramic insulated housings required by high-current, high- voltage-
transmitting circuits.
The mica capacitor is the only one of the many capacitor types that has obtained general
industry standardization for case styles and electrical ratings.
Figure 10 (a) shows outline dimensions for molded-case types, Styles 20, 25, 30, 35, 40,
45, 50, 55, 56, 60, and 61; Figs. 10(6) and (c) show outline dimensions for the potted-case
types, Styles 65, 70, 75, 80, 85, 90,
Table 5. Classification and 95.
Capacitance. Capacitance val-
ues for mica capacitors are ex-
pressed in micro-microfarads.
Capacitance
1st and 2nd digits a-nd
^- ^- multiplier
Designation
Temperature
Coefficient
Not more than
Capacitance
Drift
Not more than
Class A
±1 000 ppm
±(5% + 1 wuf)
Class B
± 500 ppm
±(3% + 1 ftftf)
Class C
± 200 ppm
±(0.5% + 0.5 jajuf)
Class I
(+150 )
±(0.3% + 0.2^/zf)
Class D
( — 50 ppm }
db 1 00 ppm
±(0.3% 4. o.l ji/rf)
Class J
(+100 i
±(0. 2% + 0. 2 /i/if)
Class E
I — 50 ppm J
f+ioo i
_j_(0 1% 4- o 1 wzf)
Class G
1 - 20 ppm j
/ 0 )
±(0 1% + 0 1 wif)
\ - 50 ppm J
White
Glass
Tolerance
FIG. 11. RMA Capacitor Color Code
(Proposed)
Color Marking of Molded Types.
Note: Characters D, J, E, and G require individual tests of A convenient ^ system of six-color
each capacitor and should be considered for use only where marking is being used to identify
extreme stability and accuracy are required. molded mica case types. Two
RMA color codes are in use, one as
a standard and the other proposed, but industry standardization is expected to
make the old system, which does not provide for identification of the class designation,
obsolete.
Figure 11 shows the arrangement of the two rows of colors, and the significance of each
color is shown in Table 6.
CEKAMIC DIELECTRIC CAPACITORS
3-67
Radio-frequency Current Ratings. The potted-case type of mica capacitor is intended
primarily for use in frequency-determining circuits or those requiring the capacitor to
Table 6
Color
Numerical
Significance
Decimal
Multiplier
Capacitance
Tolerance
Class
Designation
Black
0
1
20%
A
Brown. . . .
Red
1
2
10
100
2%
B
c
Orange
Yellow....
Green. . . .
3
4
5
1,000
10,000
3%
5%
D
E
Blue
6
Violet
7
Gray
8
I
White
9
J
Gold
0. 1
Silver
0.01
10%
15
handle appreciable amounts of r-f current. Typical curves illustrating the current-
carrying capacity for a frequency range of 0.1 to 30 megacycles of mica dielectric
capacitors housed in potted ceramic cases are shown by Fig. 12.
It is interesting to note the increasing current 2o
loading with frequency for the O.OOOl-ju/xf ca-
pacitor in comparison with the decreasing cur-
rent rating with increasing frequency for ca-
pacitance values greater than 0.001 jujuf, which
is due to the inductance introduced in the
series-paralleling of the mica sections which
constitute the capacitor stack for the larger
capacitance values.
The current-carrying capacity of mica dielec-
tric capacitors can be materially increased by
immersing the foil-mica stack in silicon oil and
removing the heat generated by means of
cooling coils.
Manufacturers' published ratings are based
on an ambient temperature of 40 deg cent,
and the current ratings must be derated for
higher ambient temperatures as shown in
Table 7.
20
= 10
Table 7. Current Deratings with Tem-
perature
Characteristic
Temperature
Range
Current
Derating
Factor
B, C
B, C
B, C
D, E, G
41 to 50 deg cent
51 to 60
61 to 70
40 to 70
0.95
0.85
0.70
0.50
16
14
12
10
8
6
4
2
0
0
*>•*
-^,
/
/
^•sv
y
/
>sv
/
X
/
1 0.2 0.3 0.5 1.0 23 5710 2JC
Commercial Specification References.
Joint Army-Navy Specification JAN-C-5, Capacitors,
Mica-Dielectric, Fixed.
RMA Standards Proposal 158A.
Frequency to megacycles
FIG. 12. Current-carrying Capacity for 10 Deg
Cent Temperature Rise (Courtesy of Solar
Mfg. Corp.)
21. CERAMIC DIELECTRIC CAPACITORS
Ceramic capacitors are neither new nor the result of any accidental discovery. They
are the direct result of long research in the early 1900's when German scientists noted the
unusual characteristics of titanate ceramic materials.
Europe has never had a domestic source of mica and was, therefore, faced with a serious
shortage before World War I. This shortage focused attention and accelerated research
3-68
RESISTORS; INDUCTORS; CAPACITORS
into the possibilities of developing a suitable substitute. This problem in ceramic research
took German scientists many years to solve. In the early 1930's, a ceramic titanate mate-
rial was finally developed that was controllable in production quantities and, at the same
time, would retain stable characteristics. These ceramic dielectric units were quickly used
in substantial quantities by European radio and electronic industries.
The ceramic dielectric because of its negative temperature coefficient was used in tem-
perature-compensating capacitors in oscillator circuits. As more experience was gained
and the basic characteristics became more clearly understood, other forms of ceramic
capacitors were used, including higher capacitances, such as by-pass and coupling types
for transmitting and other high-voltage and high-current capacitors.
The electronics industry in the United States was slow to recognize the possibilities of
ceramic capacitors and to utilize the general existing knowledge of European ceramic
dielectric materials because of the abundant supplies of mica which were readily available.
A second retarding factor was the general feeling that ceramic dielectrics in the titanate
group would be far too costly for our mass-production methods.
Centralab, a division of Globe Union, Inc., in the early 1930's, initiated a research
program to investigate the availability of raw materials and the possibility of producing
ceramic capacitors similar to the European types. Abundant domestic supplies of raw
materials were located which exhibited characteristics superior to those of the European
materials.
The first group of capacitors was offered in capacitance value up to 1000 jujuf and in
controlled temperature coefficient varying from a positive change of 100 ppm to a negative
change of 750 ppm. The dielectric constant of these materials varied from 50 in the zero
temperature coefficient group to a maximum of 95 in the group having a negative tempera-
ture coefficient of 750 ppm.
The use of ceramic capacitors was greatly accelerated during World War II because of
the increased demand for substitutes for mica capacitors, which were in short supply
owing to a shortage of high-quality mica.
The fact that ceramic capacitors possess low losses at ultra-high frequencies makes them
ideally suited for application where other types of dielectrics are not satisfactory. They
are available in both tubular and disk constructions. The disk constructions employ a
"feed-through" terminal arrange-
M-argto Silver electrodes ment which re(juces lead inductance
to the absolute minimum.
A typical construction for the tu-
bular ceramic capacitors is shown in
Fig. 13. In this construction, the ca-
pacitance is controlled by the dielec-
tric constant of the ceramic, by the
length, diameter, and wall thickness
of the ceramic tube, and by the sil-
vered area of the electrodes. Stabil-
End
Ceramic
dialectric to electrode
FIG. 13. Construction Detail: Ceramic Capacitor
Steatite
tube
soldered
ity of capacitance with temperature and applied voltage is obtained with the use of low-K
ceramics in the range of 50 to 500. The dielectric constant may be increased through the use
of titanates, but this is accompanied by a reduction in capacitance stability and a marked
increase in voltage coefficient which imposes limitations on the use of the high-.K' bodies.
Commercial Specification References.
Joint Army-Navy Specification JAN-C-20, Capacitors, Ceramic-Dielectric, Fixed (Temperature-
Compensating) .
RMA Standards Proposal 157, Ceramic Dielectric Capacitors.
22. ELECTROLYTIC CAPACITORS
Electrolytic capacitors employ solid dielectric media on which an oxide film, produced
electrochemically, is the dielectric in the presence of a d-c polarizing voltage and an ionic
conducting medium.
Investigations have shown that the oxides of tantalum and aluminum exhibit desirable
characteristics. Tantalum possesses an oxide with high dielectric constant and low
leakage, but economic factors have limited its use. Its principal limitations are voltage
rating and mechanical construction resulting from the use of sulfuric acid as the electrolyte.
Aluminum is the metal used in all other electrolytic capacitors because of its low price
and excellent film-forming characteristics.
An oxide film can be formed on aluminum by electrolytic means by immersing a ribbon
of alnTnirmm foil in an aqueous solution of boric acid and sodium borate and passing an
ELECTROLYTIC CAPACITORS 3-69
electric current through, the solution with the aluminum forming the positive pole or anode.
Electrolysis of the solution causes oxygen to be generated at the positive pole, oxidizing
the surface of the aluminum. The film thickness is a function of the d-c formation voltage.
The extremely thin oxide film formed on the aluminum anode offers a very high resist-
ance to further passage of current if the applied voltage is not increased above the film
formation voltage. A cell of this nature inserted in a container containing an aqueous
electrolyte takes the form of the so-called wet electrolytic capacitor. The aluminum oxide
film acts as the dielectric, the electrolyte as the cathode, and the container as the contact
medium for the cathode.
The electrolytic capacitor has a very high capacitance per unit volume as compared to
other types of capacitors, such as the impregnated-paper or mica dielectric types.
The primary reason why an electrolytic capacitor gives a high capacitance per unit
volume is the extreme thinness of the dielectric or oxide film. The thickness of the oxide
film covering the aluminum electrode is approximately 2 X 10"5 in., and the dielectric
constant K of the oxide layer produced is high (approximately 10) as compared with 2.5
for a mineral oil impregnated paper capacitor.
There are two types of electrolytic capacitors, depending upon the physical character-
istics of the electrolytes: the wet type, which uses an aqueous electrolyte; and the dry type,
which uses a viscous or paste electrolyte.
ANODE FOIL TREATMENTS. The anode foil employed in electrolytic capacitors
may assume several forms, depending upon design considerations:
1. Plain foil, where the oxide film is electrochemically formed on the surface of the
aluminum foil without any previous treatment of the foil surface.
2. Etched foil, where the surface of the aluminum foil is first treated chemically or eiectro-
chemically to erode the surface, thereby increasing the superficial area prior to the film-
forming procedures.
3. Sprayed gauze, where an inert carrier such as chemically pure cotton gauze is mechan-
ically coated with aluminum by means of metal spraying.
The etched foil electrode is the most common one in both wet and dry types of electro-
lytic capacitors, although the sprayed gauze construction is becoming more common in
the dry electrolytic capacitor types.
The hydrochloric acid etched anode foil construction is used in place of plain foil because
it gives effective surface areas much greater than those obtained from plain foil and
thereby cuts the physical size.
CATHODE OR COLLECTOR FOIL TREATMENTS. Filming of the cathode foil is
a very interesting phenomenon which has been observed in very high gain foils in circuits
of high ripple currents and which must be care-
fully considered in the use of electrolytic capaci- /T> • s| TL
tors. The mechanism that causes cathode film \L7 -L f j_oad
formation can be explained by the fact that the i I
cathode foil under high ripple current conditions
is subject to a reversal of ripple current due to the
charging of the capacitor on the conducting part i -A / - \ -y r ^j/ \ IAE.
of the cycle and the discharging of the capacitor Eia"cEd.c/ j \ T V
into the load on the non-conducting part of the * I / | / \ ( \ ,
cycle even though the cathode never becomes ER=peak ripple voltage
positive with respect to the anode polarizing Ea-c—chargmg voltage
potential, as illustrated by Fig. 14. As can Ed-c Average voitqge
be seen from the diagram, on one part of the IL~ Load CUPimt
cycle the capacitor is charging and during the FIG. 14. Mechanism of Cathode Formation
other half-cycle the capacitor is discharging
through the load. The result is that the cathode becomes anodized to the value of the
ripple voltage impressed across the capacitor. The value of this potential is a function
of the power-supply regulation, the capacitor impedance, and the magnitude of the load
current. When the capacitance of the cathode is reduced by formation, it produces in
effect a low instead of a high capacitance in series with the anode capacitance and reduces
the capacitance of the capacitor, depending upon the degree of cathode film formation.
Etched Cathodes. Most commercial designs employ etched cathode foil for low-voltage
sections (less than 25 working volts d-c) and for other ratings where ripple current is high.
Etched cathode foil is used for the following reasons:
1. An etched cathode foil increases the effective cathode surface area, which reduces
the ripple current density to such a value that the cathode film does not build up to a
value exceeding the initial thickness of the cathode film.
2. The increased cathode surface will afford a much higher cathode capacitance, and,
the higher the value of the cathode capacitance, the smaller will be the reduction in initial
3-70
RESISTORS, INDUCTORS, CAPACITORS
anode capacitance because of the series connection of the cathode and anode capacitance.
For example, a 100-yuf 15 working volt d-c electrolytic capacitor with a plain foil cathode
has a cathode capacitance of approximately 120 /zf , which would cut the total capacity of
the unit to 54.5 juf. However, if an etched cathode foil was used, the cathode capacitance
would be approximately 1200 jwf , and the resultant total capacitance of the capacitor would
be 93 fd .
Table 8 gives the maximum root mean square ripple currents recommended in RMA
Standards Proposal 160 A for various capacitance and voltage ratings.
Table 8. Maximum rms Ripple Current in Milliamperes at 120 Cycles
Micro-
farads
15v
25 v
50 v
150v
250 v
300 v
350 v
400 v
450 v
10
80
90
145
150
150
20
90
160
180
180
180
180
30
135
180
200
200
200
200
40
190
190
200
200
200
200
50
200
200
200
200
200
200
60
135
200
200
200
200
200
200
70
150
200
200
200
200
200
200
80
200
200
200
200
200
200
200
90
200
200
200
200
200
200
100
200
200
200
200
200
200
200
300
300
300
300
300
300
400
400
400
400
500
500
500
500
600
625
600
550
650
700
700
580
700
750
800
625
750
900
900
700
850
1000
700
850
1500
850
1000
2000
1000
Table 9. Commercial Capaci-
tance Tolerances
It is very important that electrolytic capacitors should not be subjected to ripple cur-
rents in excess of the values listed in Table 8 ; otherwise, the capacitors will overheat and
the life will be appreciably reduced.
CHARACTERISTICS OF ELECTROLYTIC CAPACITORS. A knowledge of the basic
characteristics of electrolytic capacitors is essential for
^^ C0rrect use. These are:
Capacitance. The capacitance of a dry electrolytic
capacitor is determined by the surface area of the anode
and the dielectric thickness by the formation voltage.
With etched foil construction, the increase in superficial
area or gain varies inversely with the formation voltage.
There is a problem of capacitance control with formation
voltage, since for lower voltages capacitance per unit area
varies considerably. See Table 9.
Leakage Current. The leakage-current characteristic of a dry electrolytic capacitor
represents the amount of direct current flowing through the capacitor with its rated polariz-
ing voltage applied, and does not include the momentary charging current. This leakage
current is an indication of the quality of the anode film. Commercial specifications for
permissible leakage current may be determined by the
formula: Table 10. Leakage-current
I - KC + 0.3 Constant
D-c Working
Voltage
Capacitance
Tolerance
0- 50
51-350
351-450
-10; +250%
-10; +100%
-10; +50%
where I is the d-c leakage in milliamperes, K is the constant
as shown in Table 10, and C is the rated capacitance in micro-
farads. The leakage current is determined after application
of rated d-c working voltage.
D-c "Working Voltage. The d-c working voltage is the
maximum d-c voltage the capacitor will stand under con-
tinuous operation within its normal temperature range.
Peak Working Voltage. The peak working voltage represents the d-c voltage plus the
peak a-c ripple voltage; it refers to a continuous operating condition and should not be
confused with surge voltage.
0-c Rated
Voltage
K
3 to 100
101 to 250
251 to 350
351 to 450
0.01
0.02
0.025
0.04
ELECTKOLYTIC CAPACITOES
3-71
Table 11. Single-voltage
Ratings.
D-c Rated
Voltage
D-c Surge
Voltage
3
4
10
12
15
20
25
40
50
75
150
185
250
300
300
350
350
400
400
450
450
500
Table 12. P Factors
Surge Voltage. The surge voltage is a short-time d-c voltage rating that exceeds the
peak working voltage and approaches the film formation voltage. This voltage is limited
by the internal heating of the capacitor caused by the rapid increase in leakage current
as shown by Fig. 17. Usage has established surge-voltage ratings for various d-c working
voltages which are listed in Table 11 for a 1000-ohm circuit
regulation resistance.
Power Factor. For all practical purposes, the power factor
of an electrolytic capacitor is the ratio between equivalent
series resistance and the capacitance reactance at a given
frequency. It is expressed in percentage and indicates the
energy consumed by the capacitor.
Equivalent Series Resistance. Equivalent series resistance
is a more useful characteristic in mathematical equations re-
lating to electrolytic capacitors. The equivalent series resist-
ance represents the total losses. rs = watts A"2, where ra —
equivalent series resistance and i = leakage current. The
total losses in an electrolytic capacitor consist of: (1) dielec-
tric loss of oxide film, (2) electrolyte resistance, and (3) con-
tact resistance. The combined effect of these losses is ex-
pressed as the equivalent series resistance value necessary to
produce an i2r loss of the same magnitude.
A convenient figure of merit for evaluating losses in electrolytic capacitors is the P
factor, which is expressed as the product of the rated capacitance in microfarads and
equivalent series resistance in ohms, as measured on a polarized capacitance bridge at a
frequency of 120 cycles per second. Commercial capacitors have P factors which do not
exceed the values shown in Table 12 for the several standard d-c voltage ratings. When
the high- and low-voltage sections are combined into a single capacitor winding, the elec-
trolyte for the high-voltage section determines the P factor for the low-voltage section and
raises the P factor over what would be obtained with a low- voltage electrolyte. This makes
it necessary to double the P factor (Table 12) for the low- volt age section in combination
with sections having d-c ratings exceeding 150 volts.
Temperature Effects. Capacitance, series resistance,
power factor, and impedance of electrolytic capacitors are all
somewhat affected by temperature. Figure 15 shows capaci-
tance and power factor vs. temperature for typical commer-
cial electrolytic capacitors when operated over a temperature
range of —20 to 85 deg cent.
Aircraft and other special industrial applications require
dry electrolytic capacitors which will maintain constancy of
characteristics for temperatures as low as —40 deg cent.
Special electrolytes are available which meet these require-
ments; see Fig. 16.
Dry electrolytic capacitors are not recommended for use
in ambient temperatures exceeding 85 deg cent because of
rapid drying out of the electrolyte.
Leakage current increases with temperature, as shown by curve Fig. 17 for a high-voltage
filter capacitor and low-voltage by-pass section combined in a single winding.
Dry electrolytic capacitors intended for operation at ambient temperatures of 85 deg
cent require the electrolyte to be heat-stabilized to prevent the leakage current from
increasing to the point where the capacitor overheats and fails. The dotted curve of "Fig.
18 shows the reduction in leakage current at rated d-c voltage for various temperatures
in comparison with the leakage current for these same temperatures before heat sta-
bilizing.
Early failure of dry electrolytic capacitors in electronic equipment is often due to failure
to allow for excessive temperature in the electrolytic capacitor specifications.
R-f Impedance. Multiple-section concentrically wound dry electrolytic capacitors
employ a common cathode which gives rise to coupling in the cathode circuit because of
' the common current paths as shown by Fig. 19. In circuits where common coupling
causes circuit unstability, a swedged cathode is employed. This construction effectively
cuts the common r-f impedance to a negligible value by the extension of the cathode foil
with the turns swedged together, which, in effect, gives a non-inductive cathode construc-
tion since each cathode or ground terminal is directly under its corresponding anode ter-
minal. This construction is similar as far as the cathode is concerned to the non-inductive
winding shown in Fig. 6 for impregnated-paper capacitors.
Rated Voltage
P
3
3000
10
1500
15
1200
25
500
50
400
150
300
250
250
300
250
350
250
400
250
450
250
3-72
RESISTORS, INDUCTORS, CAPACITORS
Gas Pressure,
expansion. This
100
90
80
70
£60
fso
=
f<0
s
30
20
10
°c
Electrolytic capacitors should be supplied with a libei
extra space is to accommodate any sudden generation o
al space for gas
f gas which may
50
45
40
35
30 f
25 |
1
20£
15
10
5
P
1 I
90 45
80 40
70 35
„„£ -Son
\
*^-
T"
S c
t power (act
in mlcrofara
K £
\
/
^
|
=
i-*
s
\
A
apa
citar
erat
ce
jre-
s.
V
^
,^—
/
LIII|J
\
/<
Cap
aclt
per
nee
vs.
-*r
30 15
20 10
10 5
/
\
A
/
\
-Po
-tei
wer
npe
fact
atu
3f VS
/
\
1
/
\
/
\
1
/
\
/
\
s'
,wer
mpe
fac
rati
or v
s.
/
\
-+
?
/
X
S
^
1 —
-—
n 0
tTm in n in 20 30 40' so eo'io" -30-20-10 0 10 io an 4U so bu in
"'T.mp.tSu™ in f,,,f=S4l§Sr,d°. '° T«np.r.tu« In d.l»M cuflgnKl,
FIG. 15. Capacitance and % Power Factor vs Temperature of Electrolytic Capacitor (Courtesy Solar
Mfg. Corp.)
be liberated as the result of improper uses of the capacitor. In addition, most electrolytics
are supplied with built-in vents which prevent capacitors from exploding when they are
improperly used, as being accidentally connected across alternating current.
Resistance and impedance hi chins
k
3Oli-»t-'MNilx) c
0 » 0 01 o t
n mf and power factor in per cer
\
\
Ca
/
pacit
ancs
1
\
i
K
"*
\
/[V
N
x
;
ower
fact
or
\
V
]_mpj
3 dan
:e
~~ ^
t
1
^
&*
-£q
uivaient serie
; resist a rice
2-
-60 -40
-20 0 20 40 60
Temperature In degrees centigrade
80
FIG. 16. Variation of Characteristics of Low-temperature Electrolytic Cap)
(16 /if— 350 WVDC— Courtesy of Solar Mfg. Corp.)
100 g.
<5
[tor with Temperature
Polarity. Polarized, types of dry electrolytic capacitors are designed for use in d-c or
intermittent d-e circuits produced by rectifying alternating current. D-c polarized capaci-
tors should not be subjected to reversed polarity, as the heavy current passing through the
capacitor under this condition will raise its internal temperature and seriously damage it.
10
20 30 40 50 60 70
Temperature in degrees centigrade
90
FIG. 17. D-c Leakage vs Temperature — Dry Electrolytic Capacitors
BIBLIOGEAPHY
3-73
Non-polarized Types. This term applies to dry electrolytic capacitors constructed with
two formed electrodes so that they function equally well with direct current impressed
on either electrode irrespective of polarity. This does not mean that they can be used on
alternating current continuously. Non-polarized capacitors are for applications where
the d-c voltage supply might become re-
versed and remain so indefinitely. A non-
polarized capacitor is equivalent to two
polarized capacitors connected in series
opposition.
A-c Motor-starting Capacitors. Non-
polarized dry electrolytic capacitors may
be used for intermittent duty in a-c cir-
cuits such as for motor starting, and they
are known as motor-starting capacitors.
They are ideal for intermittent duty when
used within the manufacturers' limits for
operating voltage, temperature, and duty
cycle.
Since the duty cycle is based on internal
Leakage current fa mJTItamps
pj-.HK>(oww^.i
owooio oiocnoc
/
/
£
tat
da
d-
V
/
'
^
/
/
^
^
-f
.---
^tf
—
HP
\}
sfot
pizi
pri
--
— ' '
20
100
30 40 . 50 60 70 80 90
Temperature in degrees centigrade
FIG. 18. Effect of Heat Stabilization of Electrolyte
(30 Mf— 450 WVDC— Courtesy of Solar Mfg. Corp.)
heating of the capacitor, it is possible to vary the number of application periods of voltage
with the period of duration of voltage so that the product is a constant. The manu-
facturers' guarantee is usually twenty 0.5-sec starts per hour.
The normal maximum operating temperature of these capacitors is 65 deg cent. They
may be successfully operated up to 85 deg cent provided that the duty cycle and maximum
voltage conditions are adjusted ac-
tt © t ^
Anode T T Anode ? Anode^)
l"NiU>'MUHiNt'UiUNtUni'HHmnn\ ©
Start of
winding
r.
. Coupling path
(i) Anode tab or riser
©Cathode tab
© Anode foils, three
(4) Contact foil or misscalled cathode foil
© Cathode, electrolyte-impregnated paper
FIG. 19. Schematic Diagram of Three Section Dry
Electrolytic Capacitor Winding
cordingly. However, it must be noted
that operating at higher than normal
temperatures decreases the life consid-
erably as it dries out the electrolyte at
an accelerated rate. Operation of ca-
pacitors at low temperatures cannot
harm capacitors because any change
in characteristics is only temporary at
subzero temperatures. The increase
in power factor represents an increased
resistance loss when the capacitor is in
operation, and this creates sufficient
heat to warm up the capacitor and
quickly return it to normal operating
conditions.
Commercial Specification Reference. Where more specific information and data are
required for testing methods and procedures and for specific capacitor ratings, the following
are suggested:
Joint Army-Navy Specification JAN-C-62, Capacitors, Dry Electrolytic, Polarized.
EMA Standards Proposal 160, Polarised Dry Electrolytic Capacitors.
BIBLIOGRAPHY
A.I.E.E. Standards for Capacitors, Approved Standard 18, June 1934.
Radio Instruments and Measurements, Circular of the Bureau of Standards 74, Government Printing
Office, 1924.
Maloff, I. G., Mica Condensers in High-frequency Circuits, Proc. I.R.E., Vol. 20, 647 (April
1932).
Kouenhoven, W. B., and Lemmon, C. L., Phase Defect Angle of an Air Capacitor, /. A.I.E.E., Vol. 49,
No. 11, 945 (November 1930).
Field, R. F., An Equal-arm Capacitance Bridge, General Radio Experimenter, Vol. 4, No. 8, 1 (January
1930).
Burke, C. T., Substitution Method for the Determination of Resistance of Inductors and Capacitors
at Radio Frequencies, Trans. A.I.E.E., Vol. 46, 483 (May 1927).
Gemant, A., Liquid Dielectrics, Jonn Wiley, 1933.
Morgan, S. 0., and White, A. H., The Dielectric Constant and Power Factor of Rosin Oil and Ethyl
Abietate, J. Franklin Inst., Vol. 213, No. 3, 313 (March 1932).
Hoch, E., Power Losses in Insulating Materials, Bett Sys. Tech. J., Vol. 1, No. 2, 110 (November 1922).
Benedict, R. R., Behavior of Dielectrics, Trans. A.I.E.E., Vol. 49, 739 (April 1930).
Lewis, A B., Hall, E. L., and Caldwell, F. R., Some Electrical Properties of Foreign and Domestic
Micas, Bur. Stand. J. Research, Vol. 7, No. 2, 403 (August 1931).
Siegmund, H. 0., The Aluminum Electrolytic Condenser, Bell Laboratories Reprint 349, Trans. Electro-
chem. Soc., Vol. 53, 203 (1928).
Godsey, F. W., Jr., Film Characteristics of Electrolytic Condensers, Trans. A.I.E.E., Vol. 51, 432
(Jane 1932).
3-74 RESISTORS, INDUCTORS, CAPACITORS
Godsey, P. W., Jr., A-C Capacity of Electrolytic Condensers, Trans. Electrochem. Soc., Vol. 61, 515
(April 1932).
Godsey, P. W., Jr., Cathodic Films in Electrolytic Condensers, Trans. Electrochem. Soc., Vol. 63, 223
(1933).
Godsey, P. W., Jr., Potential Gradients in Anodic Films, Trans. Electrochem. Soc., Vol. 61, 549 (1932).
Lilienfeld, Applet on, Smith, and Nieh, Studies of Fully Organized Anodic Layers on Aluminum
Trans. Electrochem. Soc., Vol. 61, 531 (1932).
Godsey, P. W., Jr., Power Losses in Electrolytic Condensers, Trans. A.I.E.E., Vol. 51, 439 (June 1932).
Christopher, A. J., and Kater, J. A., Mica Capacitors for Carrier Telephone Systems, Trans. A.I.E E
Vol. 65, 670 (October 1946).
Murphy, E. J., and Morgan, S. O., The Dielectric Properties of Insulating Materials, Bell Sys. Tech. J.t
Vol. 16, 493 (October 1937).
MacLeod, H. J., The Variation with Frequency of the Power Loss in Dielectrics, Phys. Rev. (2), Vol. 21
(January 1923).
Brotherton, M., Paper Capacitors under Direct Voltage, Proc. I.R.E., Vol. 32, 139 (March 1944).
McLean, D. A., Edgerton, L., Kohman, G. T., and Brotherton, M., Paper Dielectrics Containing
Chlorinated Impregnants, Industrial and Eng. Chem., Vol. 34, 101 (January 1942).
Palmer, H. B., Capacitance of a Parallel Plate Capacitor by the Schwartz-Christoffel Transformation
Trans. AJ.E.E., Vol. 56, 363 (March 1937).
Reed, M., Effect of Stray Capacities to Ground in Substitution Measurements, diagrams, Wireless
Eng., Vol. 13, 248 (May 1936).
Field, R. F., and Sinclair, D. B., Method for Determining the Residual Inductance and Resistance of
a Variable Air Condenser at Radio Frequencies, bibliography, diagrams, Proc. I.R.E., Vol. 21, 255
(February 1936) .
McDonald, L. J., Contours of Capacitor Rotor Plates, Electronics, Vol. 18, 126 (March 1945).
Boella, M., Direct Measurement of the Loss Conductance of Condensers at High Frequencies, Proc.
I.R.E., Vol. 20, 421 (April 1938).
Direct-reading Condenser for Substitution Measurements, Gen. Radio Exp., Vol. 10 (March 1936).
Michaelson, H. B., Gas-filled and Vacuum Capacitors, illustrations, Electronics, Vol. 17, 124 (September
1944).
Sinclair, D. B., High-frequency Model of Precision Condenser, Gen. Radio Exp., Vol. 12 (October-
November 1939).
Griffiths, W. H. P., Law Linearity of Semicircular Plate Variable Condensers, diagrams, Wireless Eng.,
Vol. 22, 107 (March 1945).
Field, R. F., and Sinclair, D. B., Method for Determining the Residual Inductance and Resistance of
a Variable Air Condenser at Radio Frequencies, bibliography, diagrams, Proc, I.R.E,, Vol. 24, 255
(February 1936).
Green, A. P., and McComb, C. T., Resonance in Mica Capacitors, Electronics, Vol. 17, 119 (March
1944).
Brinkmann, C., Self -discharge and Time Constant of the High-voltage Oiled-paper Condenser, abstract,
Wireless Eng., Vol. 20, 449 (September 1943).
Schick, W.y Temperature Coefficient of Capacitance; Its Measurement in Small Radio Condensers,
bibliography, illustrations, diagrams, Wireless Eng., Vol. 21, 65 (April 1944) ; Discussion, T. J.
Rehfisch, Vol. 21, 175 (February 1944).
Coursey, P. R., Thermal Stability of Condensers; Ceramic Dielectrics and Their Use at Low Tempera-
tures, Wireless Eng., Vol. 15, 247 (May 1938).
Floyd, G. H., Vacuum Capacitors, illustrations, diagrams, Proc. I.R.E. , Vol. 32, 463 (August 1944).
Proctor, R. F., Variable Air Condensers; Determination of Their Residual Parameters, diagrams,
Wireless Eng., Vol. 17, 257 (June 1940).
Attwood, S. S., and Bixby, W. H., Breakdown and Time-Lag of Dielectric Materials, J. Franklin Inst.,
March 1943.
Balsbaugh, J. C., Assaf, A. G., and Oncley, J. L., Dielectric Properties of Hydrocarbons and Hydro-
carbon Oils, Industrial and Eng. Chem., January 1942, pp. 92-100.
Barringer, L. E., The Relation of Chemical and Physical Structure to Dielectric Behavior, Trans.
Electrochem, Soc., Vol. LXV (1934).
Burnett, J. H., Liquid, Viscous, and Solid Dielectrics, Electric Manufacturing, August 1943.
Clark, F. M., The Development and Application of Synthetic Liquid Dielectrics, Trans. Electrochem.
Soc., Vol. LXV (1934).
Clark, F. M., and Raab, E. L., Electrical Stability of Mineral Oil-Treated Dielectrics, Industrial and
Eng. Chem., January 1942, pp. 110-116.
McLean, D. A., and Egerton, L., Paper Capacitors Containing Chlorinated Impregnants. Stabilization
by Anthraquinine, Industrial and Eng. Chem., Vol. 37 (January 1945).
Cornell, J. L, Metallized Paper Capacitors, The Solar System, Vol. IV, No. 4 (November-December
1946), Solar Mfg. Corp.
Berberich, L. J., Fields, C. V., Marbury, R. E., Characteristics of Chlorinated Impregnants in D-c
Paper Capacitors, AJ.E.E. Technical Paper 44-165 (May 1944).
Karplus, Edward, Wide Range Tuned Circuits and Oscillators for High Frequencies, Proc. I.R.E., Vol.
,33, 426 (July 1945).
Piper, J. D., Kerstein, N. A., and Fleiger, A. G., Oil Impregnated Paper, Industrial and Eng. Chem.,
September 1937, pp. 104071043.
Siegmund, H. O., The Aluminum Electrolytic Condenser, Bell Sys. Tech. J., January 1929.
White, A. H., and Morgan, S. O., The Dielectric Properties of Chlorinated Diphenyls, J. Franklin
Inst., November 1933, pp. 635-644.
Vhitehead, J. B., Liquid Insulators, T.
limmerman, C. L, The Aluminum Elec
Jerberich, L. J., and Friedman, Raymond, tttaouization ot <
Industrial and Eng. Chem., Vol. 40, 117 (January 1948).
Golding, E. W., Electrical Measurements and Measuring Instruments, Sir Isaac Pitman & Sons, Ltd.,
London.
Georgiev, Alexander M., The Electrolytic Capacitor, Murray Hill Books.
Brotherton, M., Capacitors — Their Use in Electronic Circuits, D. Van Nostrand Co.
Nersey, Philip R., Electrolytic Condensers, Chapman Hall, 2nd Ed., London, 1939.
Deeley, Paul McKnight, Electrolytic Capacitors, Cornell-Dubilier, 1938.
Ooursey, P. R., Electrical Condensers, Their Construction, Design and Industrial Uses, Pitman, 1927.
.Schwaiger, A., Theory of Dielectrics, John Wiley, 1932.
fWhitehead, J. B., Impregnated Paper Insulation, John Wiley and Sons, 1935.
SECTION 4
ELECTRON TUBES
THERMIONIC VACUUM TUBES
ART. BY A. P. KAUZMANN PAGE
1. Principles of Operation 02
2. Classifications 03
3. Definitions 03
4. Methods of Measuring Tube Currents
and Parameters 08
5. Vacuum-tube Operation 14
6. Typical Vacuum-tube Characteristic
Curves 31
MAGNETRONS
BY W. B. HEBENSTREIT
7. The Non-oscillating Magnetron 40
8. The Oscillating Magnetron 40
9. Operation of the Traveling-wave Magne-
tron 42
KLYSTRONS
BY A. L. SAMUEL
10. Klystrons (Employing Transit Time
Bunching) 51
11. Reflex Klystrons 54
12. Tube Types 57
GASEOUS CONDUCTION TUBES
ART. BY D. S. PECK PAGE
13. Gaseous Conduction 58
14. Thyratron Tubes 60
15. Voltage Limits of Thyratrons 62
16. Current Limits of Thyratrons : . . 63
17. Control Characteristics 65
18. Pulse Thyratrons 69
19. Installation and Operation of Hot-
cathode Thyratron Tubes 71
20. Cold-cathode Tubes 72
21. Pool-cathode Tubes 75
X-RAY TUBES
BY S. REID WARREN, JR.
22. General Physical Requirements 81
23. Tubes for X-ray Therapy 83
24. Tubes for Medical Roentgenography and
Roentgenoscopy 86
25. Tubes for Industrial Roentgenography
and Fluoroscopy, and for X-ray Dif-
fraction 89
4-01
ELECTRON TUBES
THERMIONIC VACUUM TUBES
By A. P. Kauzmann
As dealt with in articles 1-6, vacuum tubes in operation are characterized by a source
of electron emission; the conduction through a vacuous space, which may or may not
contain sufficient gas to affect the conduction, of a current between the source of emission
and one or more other electrodes by means of the emitted electrons; and the varying
of this current by means of variations in electrode potential to produce an electrical
response in an associated circuit. Thus, phototubes and cathode-ray tubes, though strictly
vacuum tubes, are excluded (see Section 15). Grid-controlled gas-discharge tubes (see
articles 13-21) and mercury-pool-type rectifiers (see article 21) are treated later in the
section because their special properties and applications require special treatment.
1. PRINCIPLES OF OPERATION
HIGH-VACtTCTM TUBES. The simplest form of high-vacuum tube is the diode, con-
sisting of a thermionic cathode and an anode. The cathode is heated to a temperature, de-
pending on its nature, at which electrons are emitted from its surface into the surround-
ing vacuous space. When the anode is placed at a potential positive with respect to the
cathode some of these emitted electrons are caused to flow to the anode under the in-
fluence of the electrostatic field, thus constituting a current flowing from cathode to
anode in the external circuit, since the electrons are negatively charged. Those electrons
which are not drawn to the anode return to the cathode.
Because of the mutual repulsion between the like charges of the electrons, only a def-
inite number of them may be accommodated in the space between cathode and anode
at any given anode potential, and therefore the current flowing is definitely limited.
This limiting effect is called space charge, and the current is said to be space-charge limited.
As the anode potential is increased the current increases until the total emission of the
cathode is drawn to the anode, beyond which point the current is said to be temperature
limited.
The relation between current and potential under conditions of space-charge limitation
may be represented approximately by the equation
where K\ is a constant depending on the physical dimensions of the tube.
Since the electron flow to the anode depends on the electrostatic field in the neighbor-
hood of the cathode, the current may be controlled in part by the potential of another
electrode in a position to influence this field. In the simple triode this additional electrode
consists of a gric?-like structure placed between cathode and anode. Because of its prox-
imity to the cathode, the grid has more control of the field near the cathode than the
anode has, but because of its open structure most of the electrons pass through to the
anode. When the grid is operated at a negative potential with respect to the cathode,
none of the electrons are taken by the grid.
The relation between anode current and grid and anode potentials is usually repre-
sented by the equation
ib = K*(eb + vec^ (1)
where K* is a constant depending primarily on the cathode and grid dimensions, ju is the
amplification factor of the tube (determined by the grid structure and grid-anode spacing) ,
and rj is usually between 1.5 and 2.5.
Other electrodes, usually grids, may be added to the structure, but the fundamental
principles involved remain the same. For applications of high-vacuum tubes see Sections
7, 16, 17, 19, 20, and 21.
GAS-FILLED TUBES. In a gas-filled diode, the space contains sufficient gas at a low
pressure to cause an appreciable fraction of the electrons passing between cathode and
4-02
DEFINITIONS 4-03
anode to collide with the gas molecules and thereby ionize them. The dislodged electrons
pass on to the anode as additional anode current, while the positively charged ions are
drawn to the cathode, but at a much lower velocity, owing to their greater mass, than
the electrons possess. Because of this low velocity a given positive-ion current produces
a much higher space-charge density than the same electron current. Therefore, the net
space-charge density produced by the two currents (the algebraic sum of the positive
and negative space charges) may approach zero, though the electron current is by far
the larger.
Since the limitation of current in a high-vacuum diode is due to the negative space
charge and this space charge is reduced by the positive ions, it follows that the presence
of the gas increases the current which may flow at a given anode potential. Under normal
conditions, the discharge is unstable at potentials much in excess of the ionizing potential
of the gas, the current increasing until limited by the cathode emission. For this reason,
the current is usually limited by an external resistance in series with the anode.
The relation between applied voltage and current may be expressed by the equation
where Eb is the practically constant "anode drop" of the tube and r is the load resistance.
2. CLASSIFICATIONS
Vacuum tubes in general are classified according to many different structural and
electrical characteristics.
Cathodes are directly heated if the actual emitter is also the resistance element which
supplies the heat, and indirectly heated if the heat is supplied by conduction or radiation
from a resistance element. The directly heated cathode is more efficient than the indirectly
heated, but for many applications may not be heated by alternating current. The
cathode material may be tungsten, thoriated tungsten, or oxide-coated metal. Tungsten is
the least efficient and is generally used only in high-voltage tubes. Thoriated tungsten
is much more efficient than tungsten and is used in many medium-voltage tubes (500
to 2000 volts anode potential) and some low-voltage tubes; at high voltages the emission
life may be short. Neither of these materials is used for indirectly heated cathodes.
Oxide-coated cathodes are the most efficient but (except in gas-filled tubes) are com-
monly used only in low-voltage tubes because of troubles from grid emission.
Anodes are radiation cooled, or air cooled, if no other cooling means is provided, or water
cooled if provided with means for circulating water about or through the anode. Only
high- voltage high-power (more than 6000 volts, 2500 watts rating) tubes are water cooled,
except for special high-frequency tubes.
Rectifiers are high vacuum or gas filled. For high-power high-voltage applications, gas-
filled tubes are usual, though high-vacuum tubes are used above 20,000 volts. For radio
receivers both are used, gas-filled tubes predominating in other low- voltage applications.
Triodes are classified according to voltage and power rating, amplification factor, and
special features such as designs for high-frequency oscillators, freedom from mechanical
disturbance, etc. There are so many triodes of varying characteristics that almost any
requirement can be met.
Multigrid tubes have been developed largely for specialized radio purposes, but the
screen-grid tubes, including suppressor-grid pentodes, have wide application. In the screen-
grid tube, the grid is screened or shielded from the anode, thus greatly reducing the feed-
back capacitance between plate and grid. For high-frequency voltage amplification,
these tubes are used almost exclusively.
3. DEFINITIONS
Vacuum Tube. (Electron Tube.) A vacuum tube is a device consisting of an evacuated
enclosure containing a number of electrodes between two or more of which conduction of
electricity through the vacuum or contained gas may take place.
NOTE: The term is used in a more restricted sense to mean a device of this nature designed for
such use as amplifier, rectifier, modulator, or oscillator.
Gas Tube. A gas tube is a vacuum tube in which the pressure of the contained gas or
vapor is such as to affect substantially the electrical characteristics of the tube.
4-04 ELECTRON TUBES
Mercury-vapor Tube. A mercury-vapor tube is a gas tube in which the active con-
tained gas is mercury vapor.
High -vacuum Tube. A high-vacuum tube is a vacuum tube evacuated to such a degree
that its electrical characteristics are essentially unaffected by gaseous ionization.
Thermionic Tube. A thermionic tube is a vacuum tube in which one of the electrodes
is heated for the purpose of causing electron or ion emission.
Phototube. (Photoelectric Tube.) A phototube is a vacuum tube in which one of the
electrodes is irradiated for the purpose of causing electron emission
Cathode-ray Tube. A cathode-ray tube is a vacuum tube in which the electron stream
is directed along a confined path to produce non-electrical effects on the object upon
which the electrons impinge.
NOTE: This classification includes cathode-ray oscillograph tubes, similar devices for television
reception, electron microscopes, etc.
Cathode-ray Oscillograph Tube. A cathode-ray oscillograph tube is a cathode-ray
tube in which the movement of an electron beam, deflected by means of applied electric
and/or magnetic fields, indicates the instantaneous values of the actuating voltages and/or
currents.
Diode. A diode is a two-electrode vacuum tube containing an anode and a cathode.
Triode. A triode is a three-electrode vacuum tube containing an anode, a cathode, and
a control electrode.
Tetrode. A tetrode is a four-electrode vacuum tube containing an anode, a cathode, a
control electrode, and one additional electrode ordinarily in the nature of a grid.
Pentode. A pentode is a five-electrode vacuum tube containing an anode, a cathode,
a control electrode, and two additional electrodes ordinarily in the nature of grids.
Hexode. A hexode is a six-electrode vacuum tube containing an anode, a cathode, a
control electrode, and three additional electrodes ordinarily in the nature of grids.
Heptode. A heptode is a seven-electrode vacuum tube containing an anode, a cathode,
a control electrode, and four additional electrodes ordinarily in the nature of grids.
Octode. An octode is an eight-electrode vacuum tube containing an anode, a cathode,
a control electrode, and five additional electrodes ordinarily in the nature of grids.
Multiple-unit Tube. A multiple-unit tube is a vacuum tube containing within one
envelope two or more groups of electrodes associated with independent electron streams.
NOTE: A multiple-unit tube may be so indicated, as, for example; duodiode, duotriode, diode-pentode,
duodiode-triode, duodiode-pentode, and triode-pentode.
Cathode. A cathode is an electrode which is the primary source of an electron stream.
Filament. A filament is a cathode of a thermionic tube, usually in the form of a wire or
ribbon, to which heat may be supplied by passing current through it.
Indirectly Heated Cathode. (Equipotential Cathode, TJnipotential Cathode.) An in-
directly heated cathode is a cathode of a thermionic tube to which heat may be supplied
by an independent heater element.
Heater. A heater is an electric heating element for supplying heat to an indirectly
heated cathode.
Control Electrode. A control electrode is an electrode on which a voltage is impressed
to vary the current flowing between two or more other electrodes.
Grid. A grid is an electrode having one or more openings through which electrons or
ions may pass.
Space-charge Grid. A space-charge grid is a grid which is placed adjacent to the cath-
ode and positively biased so as to reduce the limiting effect of space charge on the current
through the tube.
Control Grid. A control grid is a grid, ordinarily placed between the cathode and the
anode, for use as a control electrode.
Screen Grid. A screen grid is a grid placed between a control grid and an anode, and
usually maintained at a fixed positive potential, for the purpose of reducing the electro-
static influence of the anode in the space between the screen grid and the cathode.
Suppressor Grid. A suppressor grid is a grid which is interposed between two electrodes
(usually the screen grid and plate), both positive with respect to the cathode, in order to
prevent the passing of secondary electrons from one to the other.
Anade. An anode is an electrode to which a principal electron stream flows.
Plate. Plate is a common name for the principal anode in a vacuum tube.
Electron Emission. Electron emission is the liberation of electrons from an electrode
into the surrounding space. Quantitatively, it is the rate at which electrons are emitted
from an electrode.
DEFINITIONS 4-05
Thermionic Emission. Thermionic emission is electron or ion emission due directly to
the temperature of the emitter.
Secondary Emission. Secondary emission is electron emission due directly to the im-
pact of electrons or ions.
Grid Emission. Grid emission is electron or ion emission from a grid.
Emission Characteristic. An emission characteristic is a relation, usually shown by a
graph, between the emission and a factor controlling the emission (as temperature, voltage,
or current of the filament or heater).
Cathode Current. Cathode current is the total current passing to or from the cathode
through the vacuous space.
NOTE: This term should be carefully distinguished from heater current' and filament current.
Filament Current. Filament current is the current supplied to a filament to heat it.
Filament Voltage. Filament voltage is the voltage between the terminals of a filament.
Heater Current. Heater current is the current flowing through a heater.
Heater Voltage. Heater voltage is the voltage between the terminals of a heater.
Grid Current. Grid current is the current passing from or to a grid through the vacuous
space.
Grid Voltage. Grid voltage is the voltage between a grid and a specified point of the
cathode.
Grid Bias. Grid bias is the direct component of grid voltage.
Grid Driving Power. Grid driving power is the integral of the product of the instan-
taneous values of the alternating components of the grid current and voltage over a com-
plete cycle.
Anode Current. (Plate Current.) Anode current is the current passing to or from an
anode through the vacuous space.
Anode Voltage. (Plate Voltage.) Anode voltage is the voltage between an anode and
a specified point of the cathode.
Peak (or Crest) Forward Anode Voltage. Peak (or crest) forward anode voltage is the
maximum instantaneous anode voltage in the direction in which the tube is designed to
pass current.
Peak (or Crest) Inverse Anode Voltage. The peak (or crest) inverse anode voltage is
the maximum instantaneous anode voltage in the direction opposite to that in which the
tube is designed to pass current.
Tube Voltage Drop. Tube voltage drop in a gas- or vapor-filled tube is the anode volt-
age during the conducting period.
Anode Dissipation. Anode dissipation is the power dissipated in the form of heat by an
anode as a result of electron and/or ion bombardment.
Gas Current. A gas current is a current flowing to an electrode and composed of pos-
itive ions which have been produced as a result of gas ionization by an electron current
flowing between other electrodes.
Leakage Current. A leakage current is a current which flows between two or more
electrodes by any other path than across the vacuous space.
Electrode Conductance. (Variational.) Electrode conductance is the ratio of the in-
phase component of the electrode alternating current to the electrode alternating voltage,
all other electrode voltages being maintained constant.
NOTE: As most precisely used, the term refers to infinitesimal amplitudes.
Electrode Resistance. (Variational.) Electrode resistance is the reciprocal of the
electrode conductance.
Electrode Admittance. Electrode admittance is the ratio of the alternating component
of the electrode current to the alternating component of the electrode voltage, all other
electrode voltages being maintained constant.
NOTE: As most precisely used, the term refers to infinitesimal amplitudes.
Electrode Impedance. Electrode impedance is the reciprocal of the electrode admittance.
Transadmittance. Transadmittance between two electrodes is the ratio of the alter-
nating component of the current of one electrode to the alternating component of the
voltage of the other electrode, all other electrode voltages being maintained constant.
NOTE: As most precisely used, the term refers to infinitesimal amplitudes.
Transconductance. Transconductance between two electrodes is the ratio of the in-
phase component of the alternating current of one electrode to the alternating voltage of
the other electrode, all other electrode voltages being maintained constant.
NOTE: As most precisely used, the term refers to infinitesimal amplitudes.
4-06 ELECTRON TUBES
Control-grid — Plate Transconductance. (Transconductance, Mutual Conductance.)
Control-grid — plate transconductance is the name for the plate-current to control-grid
voltage transconductance.
Conversion Transconductance. Conversion transconductance is the ratio of the magni-
tude of a single beat-frequency component (/i + fz) or (/i — /2) , of the output electrode
current to the magnitude of the control electrode voltage of frequency /i under the
conditions that all direct electrode voltages and the magnitude of the electrode alternat-
ing voltage /2 remain constant.
NOTE: As most precisely used, the term refers to an infinitesimal magnitude of the voltage of fre-
quency /i.
Mu Factor. The mu factor is the ratio of the change in one electrode voltage to the
change in another electrode voltage, under the conditions that a specified current remains
unchanged and that all other electrode voltages are maintained constant. It is a measure
of the relative effect of the voltages of two electrodes on the current in the circuit of any
specified electrode.
NOTE: As most precisely used, the term refers to infinitesimal changes.
Amplification Factor. The amplification factor is the ratio of the change in plate volt-
age to a change in control-electrode voltage, under the conditions that the plate current
remains unchanged and that all other electrode voltages are maintained constant. It is a
measure of the effectiveness of the control-electrode voltage relative to that of the plate
voltage on the plate current. The sense is usually taken as positive when the voltages are
changed in opposite directions.
NOTE: As most precisely used, the term refers to infinitesimal changes. See also Mu Factor.
Electrode Characteristic* An electrode characteristic is a relation, usually shown by a
graph, between an electrode voltage and current, other electrode voltages being maintained
constant.
Transfer Characteristic. A transfer characteristic is a relation, usually shown by a
graph, between one electrode voltage and another electrode current.
Inter electrode Capacitance. Interelectrode capacitance is the direct capacitance be-
tween two electrodes.
Electrode Capacitance. Electrode capacitance is the capacitance of one electrode to all
other electrodes connected together.
Input Capacitance. The input capacitance of a vacuum tube is the sum of the direct
capacitances between the control grid and cathode and such other electrodes as are oper-
ated at the alternating potential of the cathode.
Output Capacitance. The output capacitance of a vacuum tube is the sum of the
direct capacitances between the output
electrode (usually the plate) and the
cathode and such other electrodes as are
operated at the alternating potential of
the cathode.
QUIESCENT POINT AND OPERAT-
ING RANGE. The quiescent point is the
point on the plate characteristic that
represents operating conditions with no
signal applied to the grid. With a load in
the plate circuit, it may be determined as
follows. For a load resistance of r ohms
the slope of the load characteristic line is
E&o i ET65 2 1/r = — AI/AJ!?, drawn from the point
Plate Voltage Ebb (Fig. 1) corresponding to the plate
FIG. 1. Tube and Load Characteristics supply voltage. The intersection y of
the two characteristic curves is the quies-
cent operating point, giving a plate voltage of EIO and a plate current of 7&0.
The plate supply voltage Ebb is divided into the voltage drop across the tube, Et,0,
and the voltage drop across the load, Ebb — Ebo-
When the plate supply voltage is varied over the range 1 to 2, the load resistance line
will shift parallel to the position shown and over the operating range 1 to 2. The inter-
sections of the load line with the tube characteristic determine the corresponding variation
in Ebo and Ibo*
WTien the plate supply voltage is constant but the tube characteristic is changed,
for example by changing the grid voltage, the intersection of the characteristics for the
changed values of grid voltage with the load line determines the change in Ibo and Ebo-
£
DEFINITIONS
4-07
In Fig. 1 a voltage in the grid circuit changes the characteristic curve so that it intersects
the load line at points 3 or 4. The projections of these points on the two axes show the
change in I bo and Ebo-
The tube characteristic, unlike the load characteristic, cannot be shifted parallel to
the initial position to represent other operating conditions, since it usually changes shape.
The tube characteristics should be known for a few voltages throughout the range of
operation. Intermediate values may be interpolated.
A-C EQUIVALENT CIRCUIT. In the circuit of Fig. 2 the a-c voltage Eg in the grid
circuit produces an a-c plate current Ip and an a-c plate voltage Ep. For small a-c voltages
FIG. 2. Triode with Resistance Load
FIG. 3. Equivalent A-c Circuit
of Tube with Resistance Load
the tube is equivalent to a generator with an internally generated voltage pEe and in-
ternal resistance rp. Figure 3 is the a-c equivalent of the circuit in Fig. 2.
From Fig. 3 the a-c plate current is
The a-c plate voltage is
The voltage amplification is
E,
rP -f- r
Ipr -
g -—
Tp -J— /
The power output of the tube is
'—••>-
£&
(4)
Figure 4 illustrates an a-c equivalent of the circuit of Fig. 2 in which the tube is repre-
sented as a generator of constant current I = gm Eg.
The a-c plate voltage is
The a-c plate current is
(7)
(8)
The constant-current form of representation is convenient for calculation when the
load consists of a number of parallel elements or when the plate resistance of the tube is
high and rp/(rp + r) approaches unity.
FIG. 4. Equivalent A-c Circuit
of Tube with Resistance Load.
FIG. 5. Equivalent Circuit of Triode
When the tube is amplifying a-c voltages at frequencies at which the capacitances of
tube electrodes, socket, arid wiring are not negligible the equivalent a-c circuit is as shown
in Fig. 5.
The capacitances marked Cgp, Cgk, Cpk represent the grid-plate, grid-cathode, and
plate-cathode capacitances (see Section 5, Article 25) . Any socket and wiring capacitances
4-08
ELECTRON TUBES
can be added in parallel. In screen-grid and other multielectrode tubes where the addi-
tional electrodes are grounded the circuit reduces to an equivalent-triode network similar to
Fig. 3.
BALLAST TUBES AND VOLTAGE REGULATORS. A ballast tube is used as a series
resistance to limit the load current. It is designed for a definite current and voltage drop.
Over the useful portion of its characteristic a large change in voltage accompanies a
small change hi current. As a result of this characteristic a large part of any line-voltage
change is absorbed by the ballast tube and a relatively small change occurs at the load.
In reading data for the characteristic curves, it may be necessary to allow a few minutes
after each change in voltage for the tube to reach its temperature equilibrium condition.
The performance may be determined graphically by a method similar to that described
for determining the quiescent operating point by plotting the line for a resistance load
with the experimentally determined current-voltage characteristic of the ballast tube.
A voltage-regulator tube is operated in parallel with the load. Its characteristic shows
a large change in current for a small change in voltage near the operating point. When
connected in parallel with the load with a suitable resistance effective in the supply voltage
source any change in the supply voltage will cause a change in the current in the voltage-
regulator tube such that the voltage across the regulator tube and load remains practically
constant.
The voltage-regulator tube is designed for a definite voltage and is operated between
specified minimurn and maximum current limits. A certain starting voltage somewhat
higher than the operating voltage is required.
The operating characteristics are most conveniently obtained in a normal operating
circuit.
4. METHODS OF MEASURING TUBE CURRENTS AND PARAMETERS
The characteristic relations between the direct voltages and currents of the electrodes
of a tube may be obtained in a static-characteristic measuring circuit arranged as in Fig. 6.
The voltages applied to the
different electrodes as illus-
trated are measured from a
unipotential cathode. If the
tube has & filamentary cathode
it is understood that, when
operating with direct-current
filament supply such as when
measuring static character-
istics, the electrode voltages
are measured from the neg-
ative filament terminal.
With alternating-current op-
eration of a filamentary
cathode, the center of the
filament is used as the da-
FIG. 6. Circuit for Measuring Static Characteristics
turn of potential and the electrode voltages are corrected for one-half of the filament
voltage. Ordinarily only the control-grid bias voltage is made more negative by approxi-
mately one-half of the peak alternating voltage on the filament.
FILAMENT OR HEATER CHARACTERISTIC. The filament or heater current is
obtained for several values of filament or heater voltage ranging from values producing
temperatures too low to give appreciable electron emission to values producing the maxi-
mum safe operating temperature. The other electrodes should be at zero voltage.
The curves are plotted with filament or heater voltage as abscissas and filament or
heater current and power as ordinates.
CATHODE HEATING TIME. The cathode heating time is defined for purposes of
measurement as the interval from the time of application of filament or heater voltage
to the time at which the rate of increase of plate current is a maximum.
If the primary winding of a transformer is connected in the plate circuit and a meter
is connected to the secondary winding, then the instant at which the rate of increase of
plate current is a maximum is indicated by a maximum reading on the meter.
The voltage at the terminals of the filament or heater should remain constant at the
rated or specified value.
Because of the very slow rate of change of plate current in the usual tube, the charac-
terisjtaes of the transformer or meter do not greatly influence the result. A step-down
METHODS OF MEASURING TUBE PARAMETERS
4-09
transformer and a current meter which is sufficiently damped though not too sluggish
.are suitable.
EMISSION CHARACTERISTIC. The emission characteristic shows the emission cur-
rent plotted as a function of the cathode heating power.
The readings are obtained with all electrodes, except the cathode, connected together
as the anode and with sumcient positive voltage applied to the electrodes to draw the
entire emission current from the cathode. Since the emission current at normal filament
power may be so great as to damage the tube, readings are taken at lower filament powers
0000.0
ooo.o
00.0
-p>
s=sss °g
FIG. 7. Emission Characteristic
only, and normal emission current is obtained by extrapolation. A suitable procedure is
as follows, the values applying to ordinary receiving tubes. Readings of cathode heating
power are taken with emission currents of 0.1, 0.2, 0.5, 1.0, 2.0, and 5.0 ma, with 45 volts
positive applied to" the anode. The results are plotted in Davisson coordinates (see Fig. 7),
which are a special system of curvilinear coordinates. If the emission follows Richardson's
temperature law and the cathode cooling follows the Stefan-Boltzmann law of radiation, the
characteristic will be a straight line when plotted in these coordinates. The observed
points may be extended or extrapolated to obtain the emission at normal filament power.
The emission characteristic for a type-80 tube plotted according to the above procedure
is shown in Fig. 7.
If the curve of the experimental data plotted in Davisson coordinates is not a straight
line this may be due to one or more of the following conditions:
1. Departure from the Stefan-Boltzmann cooling (bends downward).
2. Anode voltage too low to draw off all the electrons (bends downward).
4-10 ELECTRON TUBES
3. Effect of cooling due to heat of evaporation of electrons (bends downward). The
cooling due to electron evaporation amounts to approximately $IS watts, where Is repre-
sents the emission current in amperes and <f> represents the work function of the cathode
in volts. This effect may be considerable in transmitting tubes where the currents are
high and in tungsten-filament tubes where the work function is large.
4. Poor vacuum (gas ionization effects) (bends upward) .
5. Heating of the anode by the emission current (bends upward).
6. Progressive change in activity of the cathode.
Reliable analytical data cannot be obtained by this method when these extraneous
effects are appreciable.
ELECTRON EMISSION. Normal electron emission is determined with the filament
voltage adjusted to the normal rated value.
All electrodes in the tube, except the cathode and heater, are connected together, and
a sufficiently positive voltage with respect to the cathode is applied to them to obtain
practically the full electron emission.
For power-type tubes this test is not advisable on account of possible damage to the
tube. The method of extrapolation described under Emission Characteristic should be
used.
For receiving-type tubes a check on the emissive condition of the cathode can usually
be made safely if the time of application of the voltage is not permitted to exceed that
required for rapid reading of the emission current meter. An anode voltage of about 45
volts is used.
Since this test usually results in the liberation of gas and abnormal heating of the
electrodes, it should be postponed until after the completion of other tests, or a sufficient
time should elapse between this and other tests for clean-up and return to normal tempera-
ture conditions.
For tubes with extremely low cathode heating poiuer, such as the oxide-coated low-filament-
current types 1R5, 1S4, 1T4, etc., this test is neither reliable nor safe for the tube. In
checking the emission of tubes of this type a low filament voltage is applied and gradually
increased until a specified emission (less than normal for the particular type of tube,
usually 3 to 5 ma) is obtained. The filament voltage required to obtain the specified
emission is an indirect measure of the cathode or filament activity. This is an arbitrary
method suitable for comparing tubes of the same type.
In general a safe method for reading emission under all different conditions consists in
using a rotating contactor to apply the voltage for only a small fraction of the time. An
oscillograph is used to read the emission current which flows during the small interval
of time that the voltage is applied.
GRID CHARACTERISTIC. A grid characteristic curve shows the current in a grid
electrode as a function of the voltage on this electrode. The voltage on all the remaining
electrodes is held constant. A family of curves is obtained by using a different value of
voltage on one of the remaining electrodes for each curve.
The grid characteristic used most frequently is that of the control grid with the plate
voltage as the parameter for the several curves.
In reading data for the curves the current should not be allowed to flow long enough to
cause abnormal heating of the grid. The readings should be taken near enough together to
show any irregularities due to secondary emission or gas.
IONIZATION, LEAKAGE, AND STRAY EMISSION CURRENTS. In vacuum tubes
the normally small currents due to ionization, leakage, and electron emission from electrodes
other than the cathode, although usually negligible in the plate and other current-carrying
electrodes, may have an appreciable effect in the control-grid circuit of the tube.
The total current flowing to the negatively biased control grid may be divided into com-
ponents as follows:
1. Electrons from the cathode which reach the grid by virtue of contact potential and
initial velocities.
2. Electrons from other electrodes to the control grid.
3. Ionization current.
4. Leakage current.
5. Electron emission from the control grid.
Figure 8 illustrates the contributions of the various sources enumerated with the excep-
tion of 2, which is generally negligible.
The several components may be separated and measured by the following methods.
The leakage current is measured with a direct voltage applied between any two elec-
trodes and without any connections on the other electrodes. The tube should be operated
with normal voltages and currents until all parts have reached full operating temperature.
The filament voltage is then disconnected and the leakage currents read while the insulation
METHODS OF MEASURING TUBE PARAMETERS 4-11
•He
is at normal operating temperature. The tube should be complete with its base but
without socket or holder. The test voltage should be specified. Normal maximum op-
erating voltage is preferable.
If any of the electrodes remain hot enough to emit electrons an error will be introduced
into the leakage readings.
The grid emission can be measured by noting the current at a bias sufficiently negative
(point A in the figure) to stop the plate current, since at this point (A) the ionization
current (3) , being proportional to the plate cur-
rent, is negligible.
The grid emission is found by subtracting the
leakage current from the grid current at the point
A. If the leakage current is negligible the test
gives the grid emission directly.
A direct measurement of grid emission can be
made (when leakage current is negligible) by
connecting the test voltage between the grid and
plate without any connection to the cathode.
The positive voltage on the plate draws the elec-
trons emitted by the grid. The cathode should
be at its normal operating temperature. The
tube should be operated with normal operating
voltages for a time preceding this test, and then
quickly switched to the emission test circuit and
grid emission noted while the electrodes are still
approximately at their normal temperatures.
The ionization current (3) is the difference be-
tween the total grid current and the sum of the
leakage (4) and emission (5) currents in the range
of grid bias over which this difference is propor-
tional to the plate current. Departure from this
proportionality indicates the start of electron
current (1) to the grid.
PLATE CHARACTERISTIC. The plate char-
acteristic gives the plate current as a function of
the plate voltage, the voltages on the other elec-
trodes being held constant. A family of curves may be obtained by using a series of volt-
ages on one of the other electrodes. A series of control-grid voltages is ordinarily used
for the different curves. For examples see Figs. 21, 24, and 27.
The data for the curves are read in the static characteristic test circuit. For the range
of currents and voltages beyond the normal average values, it is sometimes necessary to
employ a method which is rapid enough to avoid heating of the electrodes. When a well-
regulated voltage source is available the voltages may be set to the desired values and a
switch closed only long enough for rapidly reading the current on a suitably damped meter.
GRID-PLATE CHARACTERISTIC. The grid-plate characteristic or transfer character-
istic gives the plate current vs. grid voltage for the condition of constant voltage on the
remaining electrodes. Such a transfer characteristic may be taken for any of the grids
of a multigrid tube. The curves generally used show the control-grid voltage as abscissa
and plate current as ordinate, several curves being plotted each for a different plate voltage.
See for examples Figs, 22, 25, and 29.
The data for the curves are obtained in the static-characteristic test circuit, the same
precautions being observed as in reading data for plate characteristics.
CONDUCTANCE. The conductance of an electrode may be obtained from the char-
acteristic curve showing the electrode current vs. the electrode voltage. The slope of
this curve at any point gives the electrode conductance at the voltages represented by
the point. The accuracy of the measurement as determined in this way from the static
characteristics may be made as good as desired by reading small current and voltage incre-
ments with sufficient accuracy.
The electrode resistance is the reciprocal of the conductance. For example, the plate
resistance is the reciprocal of the plate conductance, the grid resistance is the reciprocal
of the grid conductance, etc.
When many readings are to be made, a method of direct 'measurement is most convenient.
One means might be to re,ad the alternating current produced by a small alternating
voltage in the circuit. In general a Wheatstone bridge circuit is preferred as shown in Fig. 9.
In this circuit a small alternating voltage (about 0.5 volt, 1000 cps) is applied to ter-
minals 1-3 of the bridge. The electrodes being measured are connected to terminals 1-2,
FIG. 8. Stray Electron Currents
4-12
ELECTRON TUBES
and the bridge is balanced with r% for minimum sound in the telephone receivers. The con-
ductance of the electrode j is given by
"-Si
If the receivers are preceded by an amplifier the alternating input voltage may be kept
small enough so that the measurements are independent of the magnitude of this voltage.
. Voltages
/Adjusted
to Test
Conditions
FIG. 9. Conductance Measurement Circuit
This also reduces any narmonics produced by non-linearity of the characteristic. The
stray capacitances of the wiring and parts of the bridge should be kept low or balanced
by a suitable arrangement of parts. A variable capacitance C\ connected across r\ can be
used to balance different tube capacitances.
The voltage drop in the bridge circuit should be taken into account in determining the
electrode voltage of the tube. The inductance L provides a low d-c resistance path across
the amplifier. The blocking condensers C keep the direct current in a path of constant
resistance which simplifies the correction.
TRANSCONDTJCTANCE. The transconductance is a measure of the change in current
in one electrode produced by a voltage on another electrode. In a tube having several
electrodes the transconductance may be measured between any two electrode circuits,
FIG. 10. Transconductance Measurement Circuit
the cathode being common to both circuits. For example, the grid-plate transconductance,
or mutual conductance, may be determined from the curves for the grid-plate transfer char-
acteristic since this shows the plate current vs. grid voltage. The slope of this curve at a
certain point gives the transconductance at the voltages represented by the point.
The transconductance may be measured directly by means of the circuit of Fig. 10. An
alternating voltage as small as convenient is applied in this circuit, and the resistor r\ is
adjusted for minimum sound in the receivers. The stray capacitances due to the wiring
METHODS OF MEASURING TUBE PARAMETERS
4-13
and the tube may be balanced by means of the condenser C connected either between points
X-Y or X-Z as determined by trial. The direct voltages are supplied to the electrodes
through the choke coils Li and L%. The reactance of the choke coils at the frequency
of the applied alternating voltage should be large with respect to r% and r3. If the resis-
tances of the choke coils cause an appreciable drop in direct voltage the electrode voltages
should be corrected accordingly.
At balance the transconductance is given by
«» = £, (10>
This relation assumes that the electrode conductance is negligible. If the conductance
of electrode j is l/r?- and that of k is 1/r^ the transconductance is given by
ft._£fr*±«>A±j£ (11)
The following circuit constants will cover a range of transconductance from 1 micromho
to 10,000 micromhos.
n = 10 X 0.1 ohm r2 = 1000 ohms
10 X 1. ohm
10 X 10. ohms n = 100 ohms
10 X 100. ohms
With Li equal to 50 henrys and La equal to 10 henrys and a 1000 cps alternating voltage
the error in using the simplified equation will be less than 2 per cent if ry and rjb are greater
than 10,000 ohms and 100,000 ohms, respectively.
MU FACTOR. The mu factor is the ratio of the voltages in two electrode circuits re-
quired to maintain constant current in the circuit of any specified electrode. It may
be determined from the static characteristic curves or measured by a balance method.
For example, the amplification factor is a special case in which the control-grid voltage
and plate voltage are changed in such a way as to maintain constant plate current.
In the circuit of Fig. 1 1 the electrode in which the current is to be held constant is
connected to point A. The other two electrodes entering directly in the measurement
D.CX
Voltages,
> Adjusted
' to Testr
Conditions
FIG. 11. Mu Factor Measurement Circuit
are connected to points B and C, When r\ and ra and M are adjusted for minimum sound
in the telephone receivers, the mu factor is given by
!•?
n
The direct voltages to the electrodes under test may be supplied through choke coils L
having a reactance at the frequency of the alternating voltage which is high with respect to
4-14
ELECTRON TUBES
the resistances n, ra, and rs. The resistances of the chokes should be low enough to cause
negligible loss in direct voltage or the true electrode voltage determined by subtracting the
loss. If the electrode conductances are not negligible in comparison with n, r2> and rs a
correction should be made for this.
INTERELECTRODE CAPACITANCE. The capacitance between the electrodes of a tube
may be measured in various ways. It is preferable to read the direct capacitance between
any two electrodes rather than the total capacitance between an electrode and all other
electrodes. The readings are normally made with the tube cold and no direct voltages
applied. When the tube is heated the capacitance changes a small amount owing to
the presence of space charge, but the change is ordinarily negligible. The tube should be
complete with base, though the
A socket capacitance is not included
in the measurement. For most
reliable results, readings should
not be taken with any electrodes
disconnected, and the tube should
be mounted in a specified way
with respect to any shields. For
indirectly heated types the fila-
ment and cathode should be tied
together.
A bridge method for the meas-
urement of direct interelectrode
capacitance in a triode is shown
in Fig. 12. The capacitance to
be measured is connected to the
terminals A-B. The figure shows
the grid-plate capacitance Cgp
connected for measurement. The
effect of the grid-cathode capaci-
tance Cgjo in the circuit across r^
is ordinarily negligible owing to
the low resistance of r^ The
plate-cathode capacitance Cpk is
across the amplifier and tele-
The standard capacitance C and
When the bridge is bal-
FIG. 12. Electrode Capacitance Measurement Circuit
phone receivers, which does not affect the balance,
resistance r are adjusted for minimum sound in the receivers,
anced the capacitance is
(12)
An error in the reading may result if appreciable leakage resistance exists across Cx.
5. VACUUM-TUBE OPERATION
ELECTRON TRANSIT TIMES AND INERTIA EFFECT. Since the single electron
has a mass of 9.035 X 10 ~28 gram there will be a force acting on the electron in the presence
of an electric field which is proportional to the product of the field strength and the electron
unit o_f charge. This force will accelerate the electron, giving it finite velocities. If the
electron has started from rest and attains final velocities much smaller than the speed of
light, the velocity in practical units may be expressed as
v = 5.95 X 10 V? cm per sec
where V is in volts. It is common practice to express the velocity of an electron in terms
of the voltage in the above expression instead of the usual centimeters per second.
If, however, the velocity of the electron has been accelerated to velocities not negligible
compared to the speed of light, c, which is 3 X 1010 cm per sec, the mass of the electron,
77i, will increase in the ratio
— = 1.96 X 10-T + [(1.96 X 10-6F)2 +
(13)
where me is the mass of the electron at rest. At 100,000 volts the increase in mass is about
22 per cent, whereas at 1000 volts the increase is only about 0.2 per cent. At very high
VACUUM-TUBE OPERATION
4-15
voltages, therefore, the velocity of an electron will be less than the above expression by the
square root of mjm, the resulting velocity being
(14)
= 5.95 X 107 Vy — cm per sec
¥ m
The transit time of an electron becomes of importance at very high frequencies and as
would be expected depends upon the electron velocity expressed at some convenient point
and the distance it has traveled. The constant K in the following expressions is a factor
taking into account the geometry of the electric field and the effect of space charge, if
present, on the electric field. For all the cases where the electron has been assumed to
start with zero velocity the transit time, r, is
KD
5.95 X 107
X
(15)
where D, in centimeters, is the distance traveled from rest to the point of voltage V, in
volts. The dimensionless constant K has the following values: K = 1 for a field-free space;
K = 2 for field between parallel planes without space charge; K = 3 for field between
parallel planes with space charge.
For concentric cylinders the values of K are given in Fig. 13. The A and B curves are
for the usual case where the higher voltage is on the outside cylinder (the cathode being
7.0
6.0
5.0
r
*z
3.0
2.0
1.0
Transit T
me Factor
Space Cha
No Space
for Cylin
rge Li mi
Charge
d
ec
lea
i C
1 Diodes
^
-^
J
s'*
X
•^
TQSSS cathode radius
"*•=: anode radius D=(r-
Transit time =
KD KD 1
—it
5
sp
no
A^
^^
^X^
i-p ^
x
^
-x
S>
x^
^
•0) cm.
^^
-.-'
,-'
•^*
c.
^^^
„-•
.-
•»
-*
V/2^)
\ m '
Corollary:.
For parallel
r/r0=l=
5.95-1
planes
v-
o1' VE,
{K=!
^^
-"•"
<^
* —
•— *.
••»,
•«.
A
ace chg.
*"*— «.«^ _
-— .-
.__
— • —
.—
-,-
1. 2. 3. 4. 5. 6. 8, 10 20 30 40 60 80 100 200 300 500 700 1000
r0/r for Curves A & B ; r/r0f°r Curves A & 8
FIG. 13. Electron-transit Time for an Electron Starting with Zero Initial Velocity. Chart Includes
Cylindrical and Parallel Plane Structures in an Electric Field with and without Space Charge. (Cour-
tesy RCA Review.)
the inner one) ; the Af and Bf curves are for the case where the positive voltage is on the
inner cylinder.
In many cases one is interested in the transit time when the electron is not starting from
rest, as, for example, for the electron transit from the control grid to the screen grid region
of a pentode. For this case
sec (16)
5.95 X 107 '
where K and Z> are defined as before, Vi and Vz are the voltages of the two points between
which the electron is passing, and Vz > Fi.
THE INPUT ADMITTANCE OF VACUUM TUBES. The input admittance of nega-
tive-grid-controlled vacuum tubes may have deleterious effects especially at high fre-
4-16 ELECTRON TUBES
quencies. Its conductive component is, to a first order, proportional to the square of the
input-signal frequency. Being a power-absorbing element it will thus broaden the fre-
quency-response characteristic of the input circuit and lower the anticipated gain of the
preceding stage. Furthermore, it also varies with the tube transconductance or tube gain.
The reactive component of admittance is fortunately independent of frequency, but un-
fortunately it varies with the tube transconductance. For a triode or a pentode radio-
frequency amplifier the effect is to increase the input capacitance of the tube in the order of
1 to 2 jtt/xf as the tube gain is varied from cutoff to its maximum value. At low frequencies
this small capacitance change is made negligible by padding the input circuit with a suf-
ficiently large fixed capacitance, but at high frequencies this precaution is impractical.
These admittance variations which change with the tube transconductance may be greatly
reduced by the use of an unbypassed cathode resistor so positioned that it will be common
to both the input and output circuits of the tube.
The input conductance, gg, of a vacuum tube consists essentially of two components.
One of these components, gt, has its origin in the electron-transit time phenomena, and the
other, gLi has its origin in that portion of the cathode-lead inductance which is common to
both the input and the output terminals of the vacuum tube. Quantitatively the transit-
time loading, gt, as determined by D. O. North is
ra 17 + 35 (rs/n) 20 fa/n)2
where gt is the transit time input loading in mhos, gik is the signal-grid-to-cathode trans-
conductance in mhos, / is the signal frequency in cycles per second, n is the transit time in
seconds for an electron to move from the cathode to the plane of the signal grid, T2 is the
transit time in seconds for an electron to move from the signal grid plane to the plate,
and -Dp and vg are the electron d-c velocities at the plate and grid respectively. It should be
noted that for a well-screened tetrode or pentode the transit time, ra, and the plate velocity,
VP, are with reference to the screen grid. Also it should be noted that the grid-to-cathode
transconductance of a triode is the same as its grid-to-plate transconductance, whereas for
a pentode or tetrode the grid-to-cathode transconductance has a value equal to the grid-to-
plate transconductance multiplied by the ratio of cathode current to plate current. The
last two terms in the brackets of the above expression are only of second order of magnitude
in the conventional amplifier tubes since the ratio vp/vg is approximately equal to 10. In-
spection of this expression further indicates that considerable loading may be contributed
to the input circuit by electrons moving in the space between the control grid and plate
(or screen grid) . As a precaution in using the above relationship, the simplifying assump-
tions applied for its derivation are listed below.
1. The transit times, n and ra, are small compared to the period, I//.
2. The electrodes are parallel planes.
3. The initial velocity of the emitted electrons is zero and the emission is ample, so that
the three-halves power of voltage vs. current holds in the cathode-grid region.
4. The amplification factor of the signal grid is high, so that electrons on one side do not
appreciably influence the field on the other side.
5. The grid is an equipotential plane surface.
6. The alternating voltage at the grid is very small with respect to the effective static
grid potential.
7. The alternating voltage at the plate (or screen grid) is zero.
8. The potential between grid and plate (or screen grid) is substantially linear and free
of space charge.
That part of the input conductance, gz, which stems from the cathode-lead inductance
may be expressed to a first approximation, as shown by J. 0. Strutt and Van der Ziel, by
gL = ^FLkCgkgik (IS)
where gL is the input loading due to cathode-lead inductance in mhos, / is the signal fre-
quency in cycles per second, Lk is the cathode-lead inductance common to both input and
output circuits in henrys, Cgk is the capacitance between the signal grid and the cathode
in farads, and gik is the signal-grid-to-cathode transconductance in mhos.
Since both the aforementioned components of input loading are proportional to the signal
frequency squared and to the tube transconductance, the two effects are therefore im-
practical to measure separately. It is also difficult to measure the cathode-lead inductance.
If one estimates this inductance to be 5 to 10 millimicrohenrys for the glass miniature tubes
and 10 to 15 millimicrohenrys for the single-ended metal or loctal tubes where the lower
values are used for those tubes having two cathode leads, we find that from 10 per cent to
VACUUM-TUBE OPEEATION
4-17
about 35 per cent of the total input loading is contributed by the effect of cathode-lead
inductance.
The screen-grid lead inductance, L&, in a pentode amplifier or tetrode amplifier in-
troduces negative input loading, gi&, which quantitatively is
giA 47r2/2L4aC«i«2gi2 (19)
where / is the frequency in cycles per second, L& is the screen-grid lead inductance in
henrys, Cgigz is the capacitance between the signal grid and the screen grid in farads, and
600
500
V)
j: 400
E
=J.
^- 300
a
- 200
Q>
100
n
/
5SJ7
SSK:
/
/
/
/
/
/ /
//
/
100
| so
=t
^. 60
3
0.
» 4°
20
0
3001
jS
c
003
X
/
/
/
0 1000 2000 3000 "0 1000 2000 3000
Transconductance, jumhos Transconductance, /jmhos
800
S
•| 600
3.
•5 400
D.
C
c» 200
r\
/
X^AB7
~r>i
^
^
"6SGT
7
.X
V
'S
0 2000 4000 6000
Transconductance, //mhos
g Input, jumhos
10 £* m a
0000
3 0 0 0 O
fifiJ Z.
5AU6
^
'/
/,
^
S
^
0
Transconductance,
3500
3000
o2500
£
=^2000
J-1500
&>
1000
500
350
300
J250
3,200
g-150
Co
100
50
n
e
/
AG5
/
/
/
/
/
f
/
^
- €
AK5
/
/
/^
S
0 4000 8000 12000
Transconductance, fcmhos Transconductance, jumhos
PIG. 14. Input-loading Conductance vs. Grid-plate Transconductance for a Group of R-f Pentode
Amplifying Tubes at 100 Me.
£12 is the transconductance from signal to screen grid. This negative loading is small in
magnitude compared to the positive loading introduced by the cathode-lead inductance,
and for the typical pentode amplifier (gu » 0.2gi&, Cgig2 < Cgk, and L& « Lk) it will reduce
the total loading by only a few per cent. If, however, additional inductance is placed in
series with the screen lead it should be possible to neutralize the positive input loading
completely, with the distinct disadvantage that instability or even parasitic osculations
may be produced in the amplifier stage.
If the static tube voltages are held constant so that the electron-transit times do not vary
and the frequency only is varied, we may write the total input loading, gg, as
gg = gt + gL = gj* l (20)
where, if the g terms are expressed in micromhos and the frequency / in megacycles, the
constant K will be in the unit micromhos per megacycle squared. This proportionality
factor K is listed in Table 1 for several tube types with the static operating voltages, cur-
rents, and signal-grid-to-plate transconductances to which it applies. At frequencies
below 25 Me a conduction term negligible at higher frequencies should be added. This is
4-18
ELECTRON TUBES
due to dielectric losses and is proportional to frequency. For single-ended metal tubes this
added conduction loss, gn, is approximately equal to
gn = 0.03/
when / is in megacycles and gn is in micromhos. For the glass miniature and acorn tubes
this loss is too small to be measured accurately.
It should be noted that in Table 1 the five entries at the bottom of the list are for mixer or
converter use. Those applications where the signal is injected on an outer grid and the
local oscillator is injected on the inner grid produce negative loading. In the case of the
6L7, the signal being placed on the grid adjacent to the cathode, positive input loading is
produced as in the amplifier applications discussed.
If the grid-plate transconductance is varied from minimum bias to cutoff bias the input
loading will vary in proportion to this transconductance and a complicated function of the
electron transit times. In Fig. 14 are given in graphical form some measured values of input
loading. These data were observed at 100 Me with the static voltages of Table 1 applied.
The grid-plate transconductances were varied by changing the signal-grid bias. To com-
pute the input loading at any frequency, / in megacycles, multiply the loading at 100 Me
by the ratio (//100)2.
Table 1. Values of K, Cgiet and AC Input for Several Tube Types
Grid-plate
AC Input
Tube
Type
Plate
Volt-
age,
volts
Screen
Volt-
age,
volts
Signal-
grid
Bias,
volts
Plate
Cur-
rent,
ma
Screen
Cur-
rent,
ma
Transconduc-
tance or Con-
version Trans-
conductance,
cgk*
fj.p.t
Change
in Input
Capaci-
tance^
Input
Loading
Constant
K, ^mhos
pirnhos
/i/if
per Me2
6SJ7
250
100
-3
3.0
0.8
1650
2.5
1.0
0.053
6SK7
250
100
-3
9.2
2.6
2000
2.1
1.2
0.050
6SH7
250
150
- 1
10.8
4.1
4900
4.2
2.3
0.063
6SG7
250
125
-1
11.8
4.4
4700
3.7
2.3
0.060
6AB7
300
200
-3
12.5
3.2
5000
3.6
1.8
0.079
6AC7
300
150
-2
10.0
2.5
9000
6.4
2.4
0.175
9001
250
100
-3
2.0
0.7
1400
1.7
0.5
0.0062
9003
250
100
-3
6.7
2.7
1800
1.4
0.5
0.0066
6AK5
150
120
-2
7.5
2.5
5000
2.6
I.I
0.0134
6AG5
250
150
-1,8
7.0
2.0
5000
3.9
1.4
0.033
6BA6
250
100
-1.2
11.0
4.2
4400
3.5
2.2
0.060
6AU6
250
150
-1
10.8
4.3
5200
3.5
2.5
0.076
954
250
100
-3
2.0
0.7
1400
1.5
0.5
0.005
6J7
250
100
-3
2.0
0.5
1225
2.5
1.0
0.05
6K7
250
100
-3
7.0
1.7
1450
2.1
1.2
0.05
6A8
250
100
-3
3.5
2.7
550
-0.05
6SA7J
250
100
0
3.5
8.5
450
-0.03
6SA7 §
250
100
-2
3.5
8.5
450
-0.03
6K8
250
100
-3
2.5
6.0
350
-0.08
6L7
250
100
-3
2.4
7.1
375
0.15
* This is the capacitance between grid and cathode with all voltages applied and grid biased to
plate-current cutoff.
t This is the increase in input capacitance as the grid bias is varied from cutoff to the plate current
indicated in this table.
$ Self -excited.
§ Separately excited.
The reactive component of input admittance is essentially capacitative since the reac-
tances due to the lead inductances to the several tube elements are small up to frequencies
of the order of 100 Me. This input capacitance consists, in the typical grid-controlled
amplifiers, of the static paralleling capacitances between the signal grid and all grounded
elements plus a variable capacitance which is independent of frequency but changes with
tube cathode current and therefore varies with the tube gain.
The variable component of input capacitance may be broken down into two components.
One known as the Miller effect is due to the grid-plate or feedback capacitance, Cgp. With
a pure resistance output load in the plate circuit or one tuned to resonance with the signal-
input frequency the added input capacitance is
(1
(21)
where A is the voltage gain of the stage. In a triode this component may be of the order
of 1Q to 100 times as large as the other input capacitance components. Since the grid-
VACUUM-TUBE OPERATION
4-19
plate capacitance of a pentode r-f amplifier tube is of the order of 0.001 that of a triode,
this Miller effect can be made negligibly small with a properly designed pentode amplifier.
A second source of input-capacitance variation is due to the space charge in the cathode-
grid region. Theory predicts that the capacitance between grid and cathode, Cgk, should
increase by 33 Vs per cent when space-charge-limited current flows as compared to no
current flow. Measurements show that there is an increase with current flow but not an
abrupt one, the difference being due in all probability to the theory's assumptions of
simple geometry and zero initial velocity of emitted electrons not being fulfilled. In
Fig- 15 are shown graphically the results of measurements of input-capacitance increases
1.2
1.0
^.0.8
•30.6
a
_c
a 0.4
0.2
6SJ7
'6SK7
1.2
1,0
L0.8
t
O.S
J.
[
0.2
n
^
9003
X
^9C
01
/
0 1000 2000 3000
Transconductance, /imhos Transconductance, jumhos
. 2.0
^
6SG7
SH7-
^B7
2.5
^ 2.0
1
£ 1.0
o
n
3^U6
/s
.s
.x'e
/
/X
^
''/
,
//
A
V
/,
/
^
0 2000 4000 6000
Transconductance, jumhos
0 2000 4000 6000
Transconductance. jumhos
2.5
^2.0
0.5
"6AC7
2.5
*. 2'°
§1.5
"S
Q.
£ 1.0
o
<o.s
°c
«
AG5
^
H
AK5
X
^
^
jt-
X
) 2000 4000 60
Transconductance, jumhos
0 4000 8000 12000
Transconductance, ;umhos
FIG. 15. Increase in Input Capacitance vs. Grid-plate Transconductance for a Group of R-f Pentode
Amplifying Tubes
against grid-plate transconductance for a group of typical r-f amplifier pentodes. These
measurements were made with the plate grounded to radio frequencies at 100 Me. Static
voltages are as indicated in the previous chart, where the maximum input-capacitance
change has also been entered. The transconductance was varied by changing the grid bias.
COMPENSATING FOR INPUT-ADMITTANCE CHANGES. The undesirable
changes of input admittance as the gain of an amplifier tube is varied may be made reason-
ably constant by the introduction of negative feedback through the use of a small unby-
passed cathode resistance, rjt. For the input capacitance to have the same value at full
transconductance as it has at cutoff, the value of rk in ohms is given by
ri = A^SputJL (22)
when Cgk is the capacitance at cutoff between grid and cathode, ACinput is *ne increase in
input capacitance from cutoff to maximum transconductance, and ggk in mhos is the grid-
to-cathode maximum transconductance if the cathode resistance were by-passed with a
large capacitor. Both fixed and maximum variational capacitance values are given in
Table 1. Note that this compensation holds for any frequency.
4-20
ELECTRON TUBES
For the input conductance to have the same value at cutoff as it has at full gain, the
value of the unbypassed cathode resistor, r&, in ohms is given by
(23)
where ggk in micromhos is grid-cathode transconductance, Cgk in micromicrofarads is
grid-cathode capacitance, and K in micromhos per megacycle squared is the frequency
coefficient of input loading. This compensation is also independent of frequency.
I Generally rk will not have the same value for both capacitance and conductance com-
pensation, but practically they are of the same order of magnitude so that correcting for
one will usually improve the other. In Fig. 16 are shown graphically the effects on two
tube types of adding several different values of r&
20 U
200
J150
"1
a.
JE100
-a
8
Plate Volts =i 250
_Screen Volts =15
Suppressor Volts
_Grid Volts Varied
Unbypassed Oath
Reslstor=.r& (ohr
Frequency = 40 M
0
Typ'e-SA
C7
200
Plate Vo!ts = 250' '
Screen Volts=200
Tyj
U-6^
B7
= 0
ode"
T1S)
/
^
>x
Suppressor Volts =0
Grid Volts Varied
Unbypassed Cathode Resls
rk (ohms)
:or =
3U^
c, •
/^
Frequency = 40 N
C
?
t^.
^
• — ^
~--«^.
so
3 _gl50
£
3.
«_ °B
2J |100
0
-60-
/
/
TTC*
0 ^
--
x-~
"^x
^^
, — —
-;
..0 J
^— — •
/
/
*s-*
i.-'-
"
x
^
"^-^
b^
qf)
& 50
0
^
A
/
1 * ^ *n
X
IVs
._-
-—
•—
/
Ac
30
lo ~ 5°
0 0
-1
/
'x
^
%
.>
-6Q-
, ^.
// ^
---
\
<.
^>-
•-— ,
-. ^_
^ 4c
^•s.
•^-^
C
fin
*"" "~*
— —
^9.
-
2.5
0<J
-1
12.5
5.0 7.5 10.0 0 2.5 5.0 7.5 10.0
Plate milliamperes Plate milliamperes
FIG. 16. Input-capacitance Change and Input Loading vs. Plate Current for the 6AB7 and 6AC7
Tubes. (Courtesy RCA Review.)
It should be noted that the unbypassed cathode resistance, because it produces de-
generative amplification, reduces the gain to 1/(1 + ggk?k) of its value when r& is by-passed.
NOISE GENERATED IN VACUUM TUBES. The vacuum tube is a noise generator
having several possible sources. One important type, known as the "shot effect," stems
from the fact that the electron current consists of discrete particles which leave the cathode
in a random fashion, producing fluctuation currents uniformly distributed over all fre-
quencies. The "flicker effect" is a low-frequency phenomenon caused by small emitting
areas of the cathode constantly changing their emission characteristics. This effect is
small compared to the shot effect. In tubes having more than one collector element, such
as the screen and plate of a pentode, the random division of current produces uniform
noise currents over the whole frequency spectrum of a tube's output or plate current.
Other sources are positive-ion-emission currents, positive-ion currents produced as the
result of gas ionization, and secondary-electron emission. In the low-frequency region
may also be found microphonics due to the motion of the tube elements, and hum result-
ing from the use of an a-c power source for heating the cathode. Associated with the input
loading and therefore present only at high frequencies is another noise source which may
add appreciable noise above, say, 30 Me.
The thermal agitation or shot effect for a temperature-limited current, /, of a diode
produces a mean-square fluctuation current t2, measured in a frequency band width A/, as
given by the equation _
# = 3.18 X l(rI9I A/ (24)
where i and / are expressed in amperes and A/ is in cycles per second. It is often more
convenient to express the tube-noise generators in terms of an equivalent resistance which
at room temperature produces the same noise as the hot-cathode vacuum tube. The
mean-square thermal agitated fluctuation current for any short-circuited pure resistance is
(25)
VACUUM-TUBE OPERATION 4-21
where r is the ohniic value of the resistance; K is Boltzmann's constant, 1.372 X 10 ~23
joule per degree; T is the temperature of the resistance in degrees Kelvin; and i is in
amperes. Similarly the mean-square fluctuation voltage, e2, across the open-circuit
terminals of a pure resistance is
? = 4KTr A/
where e is now given in volts. If room temperature is assumed to be 290 deg K (81 deg
Fahr) the above expressions become
i2 = ±^_d_±^ ^L (26)
e2 = 1.59 X 10 ^r A/ (27)
By direct substitution the equivalent-noise resistance of the diode with temperature-
limited current flowing is
req = ~z (28)
Such a diode is conveniently used as a noise-signal source generator.
With the diode current limited by space charge, and provided that / is small compared
to the total available emission current, the fluctuation noise currents are reduced so that
the equivalent noise resistance for the diode becomes
req = ^ (29)
301
In triodes and pentodes, shot-effect noise is present as in the diodes and may be repre-
sented by a noise-equivalent resistance whose thermal-agitation noise at room temperature
is equal to the tube noise referred to the control grid of the tube. In pentodes the random
current distributions between the screen grid and anode produce noise usually several
times greater than the thermal noise. In the following expressions for equivalent-noise
resistances, for the pentode, the first term in the parenthesis is due to shot effect and the
second term is due to screen current fluctuation :
For triode amplifiers,
req = ~- (30)
For pentode amplifiers,
J- b ~T~ •* c2 \ S m &m /
For triode mixers,
req = | (32)
For pentode mixers,
r* ' Jf + 2^\ (33)
For multigrid converters (with inner-grid or outer-grid injection),
The following approximate relationships for triode and pentode mixers, when both the
oscillator and signal frequencies are injected in the grid adjacent to the cathode, are useful
when the data required for eqs, (32) and (33) are not available. The values "as amplifier"
refer to conditions at the peak of the assumed oscillator cycle which is usually very close to
zero grid-bias.
gc (as converter) = gm/4 (as amplifier)
/6 (as converter) = /6/4 (as amplifier)
Ic2 (as converter) = ZC2/4 (as amplifier)
req (as pentode converter) = 4req (as amplifier)
T-gQ (as triode converter) — 6.5req (as amplifier)
Conversion from noise-equivalent resistance to noise-equivalent rms voltage is effected by
use of eq. (27) :
VP = 1.3 X 10~10 Vreq A/ (27a)
4-22 ELECTRON TUBES
Conversion from noise-equivalent resistance to noise-equivalent rms current is effected by
use of eq. (26) :
V? - 1.3 X 1CT10 V— (26a)
^feq
The symbols in the above equations have conventional significance whose definitions are:
req, noise-equivalent resistance, ohms.
gm, grid-plate transconductance, mhos.
gc, conversion transconductance (frequency converters and mixers), mhos.
J&, average plate current, amperes.
JC2, average screen-grid current, amperes.
Io, average cathode current, amperes.
Ve2, noise-equivalent rms voltage for band width A/, volts.
Vi2, noise-equivalent rms current for band width A/, amperes.
A/, effective band width, cycles.
In Table 2 is a listing of representative receiving-tube types showing equivalent-noise
values. Several, covering a large range of equivalent-noise resistance values, show meas-
ured values all in good agreement with values computed from the above relationships.
Positive-ion noise produced by collision ionization results from residual gas in a vacuum
tube. This very undesirable fluctuation noise may be investigated in order to determine
the magnitude of grid current (positive-ion current) which may be tolerated from analysis
of the following equation for the equivalent-noise resistance, req (gas) :
req. (gas) = (20^ + A -^ J Iig ohms
\ Sin /
(35)
where r — grid-circuit resonance impedance, ohms.
Jo = cathode current, amperes.
lig = positive-ion current to grid, amperes.
gm = grid-plate transconductance, mhos.
A = coefficient of the order of 40,000.
The term 20r2I^ represents shot-effect voltage fluctuations produced by the gas current
flowing in the grid circuit. It may be increased several fold by induction effects associated
with the ion transit time, even at frequencies of a few megacycles. The second term is
the noise generator term within the tube. If, for an example, we assume r as IO6 ohms,
gm as 2000 X 10~6 mho, Jo as 10"2 amp, and a grid current of 10~6 amp, the resulting
req. cgas) is 250,000 ohms. To reduce this equivalent-noise resistance to a value negligible
compared to the noise produced by the grid circuit resistance, here assumed to be 100,000
ohms, calls for a reduction of the gas current some 100 fold or to 10"2 microampere.
Equation (35) is applicable to triodes or pentodes.
There is a source of current fluctuations associated with the component of tube input-
conductance produced by electron transit time effects, a source which becomes important
when the input frequency is high enough to make the transit-time input conductance
relatively large. The random variations in space current will induce current fluctuations
in the control-grid circuit, giving rise to grid-voltage fluctuations proportional to the total
input impedance (tube and circuit) . These induced mean-square grid-current fluctuations
may be expressed thus:
V«"f (l-ljIXTuitf-
Inserting the value for Boltzmann's constant K, and assuming the cathode temperature,
Tfc, to be 1000 deg K, the above expression simplifies to
^2 = 7.5 X lO"20^ A/ amperes (36)
The noise-equivalent rms voltage for the band width A/ appearing at the tube control-grid
may be deduced from the above expression; it is
2.75 X IQ-iQ f volts (37)
S + gg
when gg in mhos is that portion of the tube input conductance traceable to electronic load-
ing alone; g in mhos is the grid-circuit resonance conductance; and A/ in cycles is the effec-
tive band width of the amplifier. As an example, assume the input circuit resonance
impedance to be 20,000 ohms so that its reciprocal g is 50 X 10"* mho; let gg be 200 X
VACUUM-TUBE OPERATION
4-23
I
0>
H
c4
111
* S
i-S o
..... .«-. ,.~
*¥
J'o £
equivalent
istance
Measured
Ohms
o
0
-0 $3 ° 0000
— O Jt^ ^ O vA C3 ^
^ ~ 0 °" "^ °"
.§«
•73 S
1°
o
rs CM — CM
1 I
. «j
D 0
gRgggSMRRgggsJsSM
£*
H
^_^^._ N«_m_ ^.
||
«.««m2c.«S-, ««-- -
a I
a
_ __ ^- ^_ —
1
£j CU
u-,
d
^ si
«o.«_o.*_^
§
*l
^ °^ H 2 ^ ^ ^ ^ ° *** °* ^ ^ ^ ^ ^ M
ii
??T7?OC=>?0?T?7 i T I i i i
!
S "o
oou-^ooi-nootno 00*00 o
'o
03 00
0000000000000000000
s£
CM^COCM CMCM ^--COCMCM
1
1
a
<!
iiiiis s'i'gi-i'i-i'l'il'i'C'i
i
CM CM CM CM
00 00 00 00
a
I '1^
xO* ** 35
3 ill
? ^ .-§
^ o^g
13 -2 a 3
|11i
r- ^ O qj
-rt /=? a> R
4-24 ELECTRON TUBES
mho and assume the effective band width to be 5000 cycles. The rms noise voltage appear-
ing at the signal grid is then 1.1 X 10 "^ volt, certainly not negligible for a high-gain
amplifier!
DISTORTION INTRODUCED BY R-f AMPLIFIER TUBES. Owing to the inherent
curvature of the plate-current vs. signal-grid-voltage characteristic of all r-f amplifier
tubes, there are present in the tube output three types of distortion when the input signal
has the form of an amplitude-modulated carrier. By means of a Taylor expansion series
(see also Section 5, articles 16-24), the plate current about any given operating point may
be written
r , Mb
^6 = I,o + e,-
In this expression dib/dec is the slope or transconductance, gmQ, of the plate-voltage vs.
grid-bias curve, and dHb/dec2 and S3ib/d3ec are the second and third derivatives respectively
of this same curve. The quantity eg is the alternating part of the grid voltage or the signal
input voltage. If an amplitude-modulated carrier signal voltage of the form
eg = EI(\ -j- ™>i sin pt) sin ccit
is inserted in the above series, we may neglect all the terms having harmonic frequencies
of coi : if it is assumed that there is a tuned circuit in the output of the tube which band-
passes only those frequencies and the sideband frequencies associated with the carrier
frequency OH. Two types of distortion become apparent from this operation. The modu-
lation factor, mi, is changed, and the modulation-frequency component has amplitude
distortion which" is indicated by the presence of harmonic terms of p, the modulation
frequency.
The modulation factor is thereby changed by the ratio
3 A
8 / gmo J
The amplitudes of the second and third harmonics producing amplitude distortion of the
modulating frequency are expressible as: (a) Second harmonic distortion (ratio of the
amplitude of sin 2pt to the amplitude of sin pf) .
Ratio of 2nd harmonic to fundamental — — mi — - - - E\2 (40)
l_16 gmQ J
(b) Third harmonic distortion (ratio of the amplitude of sin 3pt to the amplitude of sin p£) ,
Ratio of 3rd harmonic to fundamental = — r mi2 — - - - E-? (41)
L 32 gm0 J
A third type of distortion occurs when a second, and usually an unwanted, signal modu-
lates the desired signal. This is known as "cross modulation."
If there is substituted in the above series, for es, eg — Ei(l + mi sin pt) sin u>it +
^2(1 + W2 sin q£) sin corf where the subscripts 1 apply to the desired signal and the sub-
scripts 2 apply to the undesired signal, then the cross-modulation ratio is
Cross-modulation ratio = |~i — dH*/de*^\ $? (42)
l_2 mi gmQ J
Inspection of the three different distortion types indicates that all are proportional to the
square of the signal voltage amplitude and that all also are proportional to the third
derivative of plate current to grid voltage and inversely proportional to the transconduct-
ance. It should also be noted that, since this analysis discards all higher derivatives than
the third, reasonably small signal voltages are implied.
It is rather tedious to obtain sufficient points for an if, vs. e\ curve to determine the third
derivatives accurately by graphical means. A more practical method is to use a conven-
tional gm bridge having a calibrated and variable signal grid voltage. The procedure is to
apply a small signal, of the order of 0.01 to 0.1 volt, to the signal grid, with which a bal-
ance is established which gives a transconductance reading equal to gmQ, The bridge is
then set off-balance by a predetermined small amount, say 1 to 5 per cent, and the input
signal is increased until the bridge is again in balance. The required change in gmQ bal-
ance may be either positive or negative, depending on the curve shape. It can be shown
by application of the Taylor's series that
8 gmQ
VACUUM-TUBE OPERATION
4-25
where EQ is the peak value of the large signal applied to the grid. Substitution of the above
into the previous distortion equations results in the following expressions:
Per cent change in modulation = 2(1 mi2 ) — — X 100
\ 8 / gmQ
Per cent 2nd harmonic distortion — ~mi — ^ X 100
2 gmQ
Per cent 3rd harmonic distortion = - mi2 — —
4 gmo
Per cent cross modulation = 4 — X 100
100
If it is assumed that mi — I, that m%/mi — 1, and that the transconductance is changed
1 per cent, the above may be expressed to show the relative magnitudes of the various
distortions, giving
Modulation change = 1.25%
2nd harmonic distortion = 1.5%
3rd harmonic distortion = 0.25%
Cross modulation = 4%
In Fig. 17 are plotted the signal voltage necessary to change the gm by 3 per cent vs. the
Signal, in volts rms, to give a
3 per cent change in transconductance
OO f-» K> UJ 4^> Ui C
1
\
6K7 maximum transconductance =
6AB7 ' "
= 1450 jumhos
= 5000 jumhos
1
\
1
\
1
6K7H
I
\
1
\
F
V
\
/
1
\
**
•s,
y
1
\
^
**<*»
N
s
\
\
6AB7/
^
\
s
V.
/
\
\
*****
+ <^
"\
/
.1 1.0 10 1C
Transconductance in percent of maximum transconductance
FIG. 17. Comparison of Signal Voltages Applied to the Remote and Semi-remote Cutoff Tube Types
6K7 and 6AB7 Respectively to Produce the Same Amount of Distortion
transconductance in terms of the maximum transconductance. For modulation factors
of unity, this corresponds to saying that the signal voltages indicated will produce
Modulation change — 3.75%
2nd harmonic distortion = 4.5%
3rd harmonic distortion = 0.75%
Cross modulation =12%
The one curve is for a "remote cutoff" tube, 6K7, which requires approximately 45 volts
bias to reduce its maximum transconductance of 1500 jLonhos to about 10™3 this value.
4-26
ELECTRON TUBES
The second curve is for a "semi-remote cutoff" tube, 6AB7, which requires about 22 volts
bias to reduce its maximum transconductance from 5000 to 10~3 this value. It is apparent
that the 6K7 can handle a much larger signal than the 6AB7. The 6AB7 tube is limited
to lower signal values because of its higher transconductance value, and if it were designed
to have a similar cutoff as the 6K7 it would draw exceedingly large plate currents when
the bias was set low for maximum gain. There is thus a practical limitation governing
the maximum transconductance and
maximum signal-handling capacity
that can be designed into a tube.
CHANGING OPERATING CON-
DITIONS. Operating Voltages. It
is sometimes necessary to change the
operating potentials of an amplifier
or a power output triode or pentode
tube from the published typical op-
erating conditions. By means of the
conversion factor chart, Fig. 18, it is
possible to determine the new volt-
ages, currents, transconductance,
plate and load resistances, and power
output. The curves are based on
the fact that, if all applied voltages
(except heater voltage) are changed
by a factor n, the resulting currents
will all be changed by ns/2, the gm by
n1/2, and the plate resistance by n5jz.
The accuracy of the chart is reason-
ably good for small changes, but for
large voltage changes exceeding 2.5
to 1 the chart is unsuitable. As an
example, assume a pentode with the
following typical ratings :
Plate voltage 250 volts
Screen voltage 250 volts
Grid bias ? - 18 volts
Plate current 32 ma
Screen current 5.5 ma -
Plate resistance 70,000 ohms
Transconductance 2,300 Aimhos
Load resistance 7,600 ohms
Power output 3.4 -watts
j
3.0
1U
8
6
4
3
u?
E
2 1.0
0
£0.8
.2
gO.6
c
o
O
0.4
0.3
0.2
n.i
/
i
1
I
j
/
I
/
i
y
^
\
"V,
^
i
^
^t
n
^^^^
*s
^
/
I
"^^
s*
//
"\^
s*
/
/
\
/
1
/
1
/
/
/
F,
applies to plate, screen,
and contro grid voltage. —
applies to plate and screen
current,
applies to power output,
applies to plate resistance ~~
and load resistance,
applies to mutual
conductance.
/
/
Fp
/
/
*
jm
0.4 0.6 0.8 1.0 1.5 2.0
Voltage Conversion Factor, Fe
FIG. 18. Conversion Factor for Triode and Pentode
It is desired to determine the opera-
tion characteristics for a plate volt-
age of 100 volts. All voltages will
have to be changed in the ratio of
100 to 250 (e.g., Fe, the voltage conversion factor, is 0.4). From the chart the new to the
old ratios are picked off so that Ft is 0.25, Fp is 0.1, Fgm is 0.63, and Fr is 1.6. The new
conditions will then be
Plate voltage 100 volts
Screen voltage 250 X 0.4 =100 volts
Grid bias - 18 X 0.4 = -7.2 volts
Plate current 32 X 0.25 = 8 ma
Screen current 5.5 X 0.25 = 1.4 ma
Plate resistance 70,000 X 1.6 = 112,000 ohm
Transconductance 2,300 X 0.63 = 1,450 /tmhos
Load resistance 7,600 X 1.6 » 12,000 ohms
Power output 3.4 X 0.1 = 0.34 watt
It should be noted that this chart cannot be used if only one voltage is varied.
Changes in Heater or Filament Voltage. Changing the heater or filament voltage of a
tube will increase or decrease the temperature, current, and power input of the emitting
cathode. The curves of Fig. 19 show these relationships, which were based on taking
average values of radiation coefficients and resistivity of tungsten, molybdenum, tantalum,
and nickel covering temperature ranges of 1000 to 2800 deg. K. With a maximum fila-
ment voltage variation of ±25 per cent, engineering accuracy holds for vacuum and
VACUUM-TUBE OPERATION
4-27
gas-filled tubes, the greatest deviation between observed and predicted currents and power
input being only 4 per cent.
As an example assume that a 6.3 volt 0.3 amp heater is running with a cathode tempera-
ture of 1050 deg K and a heater temperature of 1400 deg K and that the heater voltage is
decreased to 5.5 volts or 87.3 per cent of nominal. From Fig. 19 we find that the resulting
power input is 80 per cent of 1.89 watts, or 1.51 watts. The new filament current is re-
duced to 92 per cent of 0.3 amp, or 0.276 amp, and the cathode and heater temperature
are reduced to 95.8 per cent, or 1005
and 1340 deg K, respectively.
Maximum Allowable Grid Resist-
ance. Common practice is to apply
the d-c bias to the negative control
grid of an amplifier through a series
grid resistor. It is desirable to make
this resistor as high valued as possible
since it shunts the signal source and
therefore absorbs power and may have
detrimental results on the frequency
response and loading of the signal
source. Its limiting value is usually of
the order of 0.1 to 10 megohms and is
established by the radio-tube manu-
facturer on the basis of life tests and
maximum expected grid current. Grid
current flowing through the grid resis-
tor decreases the grid bias by the IR
drop through the resistor and may
cause the tube to "run away" since
the resulting increase in plate current
will produce excessive plate dissipa-
tion. By the addition of a cathode
self-bias resistor, or the use of a series
dropping resistor in the screen lead of
a pentode, or the use of a d-c load re-
sistor in the plate lead of a triode,
there results some d-c degeneration,
thereby making it possible to increase
the value of the grid resistor above
that indicated as a maximum. Also,
if the tube is operated at a reduced
value of transconductance, the maxi-
mum allowable grid resistance value
may be increased.
From the following equation it is
possible to determine the maximum allowable value of grid resistance, rgi, for any new set
of operating conditions differing from those published.
Per cent of basic watts, current, temperature
^OTO>->JOOU)Ol-' 10 W £» 01 O> v
ooo ooooo oooooc
/
f
/
f
/
/
*~~/
/
/
/
&**~
/
/
^
^
^
^
*^e
tf&
*s
*7
""cfe^
/"
/
/
/'
/
#/
w
/
/
f
/
^/
50 70 80 90 100 110 120 130 14
Per cent of basic-voltage
Chart Giving Wattage, Current, and Temper-
, Heater, or Cathode at Operating
FIG. 19.
ature of a Filament, '. . , _.. . , _
Voltages up to 25 Per Cent above or below Basic Voltage,
with Sufficient Accuracy for Most Engineering Purposes.
Accuracy drops in dotted regions.
(44)
where, for a triode,
A7VAIffl is the ratio of plate current change per unit change in grid current;
gk is the grid-plate transconductance in mhos;
r is the d-c plate load resistance;
rp is the internal tube plate resistance;
rjc is the cathode self-bias resistance in ohms;
p is the triode mu;
and where, for a pentode,
A7fc/AIgl is the ratio of cathode current change per unit change in grid current;
gjc is the signal-grid-to-cathode transconductance in mhos (this may be determined by
multiplying the signal-grid-to-plate transconductance by the factor (Ip ~h Ic^/Ip)'*
r is the screen dropping resistance;
TP is the internal tube screen resistance;
Tk is the cathode self-bias resistance, in ohms;
{j, is the triode connected amplification factor, i.e., the mu from control grid to screen
grid of the pentode.
4-28
ELECTRON TUBES
CUtho-d-e Mis | 1.4
2.0 1 2.5-5.0 |
6.3
| 12.6-117
Kinescopes
Projec-
tion
magnetic deflection
5TP4
Directly
Viewed
magaetie deflect ion
9AP4
12AP4
7DP4
10BP4
electrostatic
dfrlectioon
7JP4
Rectifiers (for rectifiers with amplifier units, see Power amplifiers)
Half-
wave
Y3C1LU.K1
IB3-GT/
8016*
1-v
81 f
12Z3F 35W4 1
35 Y4 35Z4-GT
35Z3L35Z5-GTJ
45Z3 45Z5-GT
11 723
Full-
wave
vacuum.
5T4, 5W4
r5U4-G,5X4-G]
I 5Z3 j
T 5Y3-GT 1
5Y4-G
L 80 J
5Z4
[5V4-G, 83-v]
f 6X4, 6X5 I
L6X5-GT, 84/6Z4J
6ZY5-G
7Y4
7Z4
raereiuy-T^por
82 83
gas
Cold-Cathode Types: OZ4, OZ4-G
Dcrabler
vacuum
f 25Z5 I
25Z6
|_25Z6-GTJ
50Y6-GT
117Z6-GT
Diode -detecctow C/or diode detectors with amplifier units, see Voltage amplifiers and also Power amplifiers)
One diode
1A3
I
6AL5 [6H6, 6H6-GTJ 7A6 | 12H6 12AL5
ler amplifiers with and without rectifiers, diode detectors, and voltage amplifiers
Triodes
low-ma
snngle innit
31
49
2A3 45
46 71-A
6B4-G 10f 6A5 50 1
b igh-o"U
snngle iBnit
6AC5-GT
tinn unit
1G6-GT
T1J6-G1
L 19 J
53
[6A6, 6N71 A77 r 70
L6N7-GTJ 6Z7'G 79
direot-eoirpled
arrangement
6B5
Beam
Tubes
single unit
f 1Q5-GT 1
L3Q5-GT tl
1T5-GT
3LF4I
6BG6-G T 6AQ5 ~|
[6L61 L6V6-GTJ
L6L6-GJ
6Y6-G 7A5 7C5
14A5 r 25L6 1
35A5 L25L6-GTJ
[35B5 35L6-GT]
50A5
[50B5, 50L6-GT]
witk recfciffier
32L7-GT
70L7-GT
ri17L7/M7-GTl
L 117P7-GT J
117N7-GT
Pen-
todes
single unit
1A5-GT
1C5-GT
1LA4, 1LB4
[1S4, 3S4|]
[3Q4t,3V4JI
f 1F4 ]
L1F5-GJ
1G5-G
1J5-G
33
2A5
47
59
6A4/LA [6AK6, 6G6-G] 6AG7
[6F6, 6F6-G, 6F6-GT, 42]
[6K6-GT, 41]
7B5 .38 89
[25A6]
L 43 J
with nwdruiHEni
triode
6AD7-G
with, diode ani
triode
1D8-GT
with. recfciSer
12A7
twk unit
1E7-G
* Cathode volts, 1.25. f Cathode volts, 7.5.
PIG. 20. Receiving Tube Classi-
VACUUM-TUBE OPERATION
4-29
Cathode Volts | 1 .4
2.0 |2.5-5.0|
6.3
12.6-117
Converters & mixers (for other types used as mixers, see Voltage amplifiers)
Con-
vert-
ers
pentagrid
1A7-GT
1LA6
1LC6
1R5
[ 1C6 ]
11C7-GJ
r 1A6 1
11D7-GJ
2A7
T 6A7, 6A8 1 [6BE6, 6SA7]
6A8-G, 6A8-GT L 6SA7-GT J
L 6DS-G J
6SB7-Y 7B8 7Q7
12A8-GT
[12BE6, 12SA71
L 12SA7-GT j
14B8 14Q7
triode-hexode
[6K8, 6K8-G]
I2K8
triode-heptode
6J8-G 7J7 7S7
14J7
octode
7A8
Mixers
pentagrid
[6L7, 6L7-G]
Electron-ray tubes
Single
with remote-cutoff
triode
6AB5/6N5 6U5/6G5
with sharp-cutoff
triode
2E5
6E5
Twin
without triode
6AF6-G
Voltage amplifiers with and without Diode Detectors; Triode, tetrode, and pentode detectors; oscillators
Triodes
medium-
mu
single unit
1G4-GT
1LE3, 26 §
[1H4-G1
L 30 J
27
56
6C4 [6C5, 6C5-GT] [6P5-GT, 76]
[6J5, 6J5-GT] 6L5-G, 7A4, 37
12J5-GT
14A4
with r-f
pentode
6F7
with power
pentode
6AD7-G
with
pentode
and
diode
1D8-GT
3A8-GT
with, two
diodes
T1B5/25S]
L 1H6-G J
55
[ 6R7.6R7-GT 1 7FA R,
L6BF6, 6SR7, 6ST7J /Jit) w
f I2SR7 I
L12SR7-GT J
14E6
twin unit
6C8-G [6F8-G, 6SN7-GT] 6J6
7N7 7F8 12AU7
12AH7-GT
12AU7 12SN7-GT
HN7
high-mu
single unit
f 6F5, 6F5-GT 1 ,Trr PT «,,
L6SF5, 6SF5-GTJ 6K5"GT /B4
T12F5-GT]
L 12SF5 j
with diode
1H5-GT
1LH4
with two
diodes
2A6
F6SQ7, 6SQ7-GT] r 6AT6, 6AQ6 '
L 6B6-G, 75 J 6Q7, 6Q7-G
6T7-G, 7B6, 7C6 !_6SZ7, 6Q7-GT.
[12AT6, I2Q7-GTJ
14B6
[12SQ7r 12SQ7-GT]
with three
diodes
6S8-GT
twin unit
6SC7 6SL7-GT 7F7 12AX7
12SC7 I2AX7
12SL7-GT 14F7
Tet-
rodes
remote cutoff
35
sharp cutoff
32
24-A
36
Pen-
todes
remote
cutoff
single unit
IT4
1P5-GT
34
riD5-GPl
L 1A4-P J
58
F6K7, 6K7-G1 P 6D6 ][6BA6,6SG7]
L6K7-GT, 78J [6U7-GJ 6BJ6
6AB7/1853 [ 6S7 1 7A7, 7B7
r 6SK7 ] L6S7-GJ 7H7
L6SK7-GTJ 6SS7 39/44
[12BA6, 12SG7]
f 12SK7 I
L12SK7-GTJ
12K7-GT, 14H7
14A7/12B7
with triode
6F7
with diode
6SF7
12SF7
with two
diodes
2B7
[dBS, 6B8-G]7137 7R7
12C8, 14R7
sharp
cutoff
single unit
1LC5, 1LN5
1L4, 1U4
1N5-GT
PE5-GP1
L 1B4-P J
15
57
F6J7, 6J7-G, 6J7-GT] f 6SJ7 1
L 606, 6W7-G, 77 J L6SJ7-GTJ
r6ATI61 6AC7/1852 6AG5
L6SH7J 7G7/1232 7C7
7L7 7V7 7W7
[I2AU6, 12SH7]
12AW6
f 12SJ7 ]
U2SJ7-GTJ
12J7-GT 14C7
with diode
1LD5
[1S5, 1U5]
with two
diodes
r 1F6 i
L1F7-GJ
t Filament arranged for either 1.4- or 2.8-volt operation,
fication Chart. (Courtesy RCA.)
§ Cathode volts, 1.5.
4-30 ELECTRON TUBES
All the above factors can usually be obtained from published tube characteristics or are
measurable for a given tube type with the exception of the ratio A/fc/AIgl. This ratio
indicates that for any given amount of grid current flow there is a definite increase in
cathode current flow. If it were possible to manufacture vacuum tubes so that with a
negative grid absolutely no grid current flowed, the series-grid resistance could be infinite
in value. However, for practical tubes, grid currents of the order of a microampere may
exist due to residual gas ionization, thermal and photoelectric emission, and leakage cur-
rents. This ratio, AIjb/AI^, for a given tube may be determined from the published max-
imum allowable grid resistance by substituting it in the above equation, and once de-
termined it may be used to determine a new value of maximum resistance for a new
operating condition.
Example. A pentode with fixed bias and fixed screen voltage has indicated a maximum allowable
grid resistance of 0.2 megohm. What is the maximum grid resistance with full self-bias and a series
dropping resistance from a 300-volt supply? What is the maximum grid resistance if the bias is in-
creased so that the cathode current is reduced to one-tenth its maximum value?
For rgi — 0.2 megohm,
Egl «=* — 2 1/2 volts
EC2 — 100 volts
ECZ — 0 volts
Eb = 250 volts
M12 = 25
r2 — 25,000 ohms (internal screen resistance)
z"c2 = 2.5 ma
ip — 10 ma
The cathode transconductance, gift, is determined by,
„ = ^ «L±^>
Then n = — - ( — ) , since there are no self-bias or screen dropping resistors used. Then
Al£l \gk/
^L = rigk = (0.2 X 106)(6250 X 10~6) = 1250 (46)
Al*i
For the new conditions the self-bias and series dropping screen resistors are
rk = 2.5/(12.5 X 10~3 amp) = 200 ohms
r£2 = (300 — 100)/(2.5 X 10~3 amp) = 160,000 ohms series dropping screen resistor
The new maximum grid resistance is
^-^[&0 + aJ^Mo)^(^g)]
= 632,000 ohms
At one-tenth normal cathode current the new bias is computed to be approximately —3.7 volts, assum-
ing that the tube obeys the three-halves power of effective voltage law. The new values are then
rk » 3.7/(1.25 X 10~3 amp) = 2950 ohms
ri2 = 160,000 X 10 = 1.6 megohms series screen resistor
Tg2 = 25,000 (10)^ = 53,000 internal screen resistance
gk = 6250 X 10~6/10^ = 2910 X 10~6 mho
From the above the new maximum grid resistance is
•*"*» [^(^leT^)^850^^)]
«= 4.7 megohms
RECEIVING TUBE CLASSIFICATION CHART. Figure 20 classifies the commonly
used receiving tubes according to their functions and their cathode voltages. It is arranged
to permit quick determination by the tube user of the type designations of tubes applicable
to specific design requirements. Types having similar characteristics and in the same
cathode-voltage groups are bracketed.
TYPICAL VACUUM-TUBE CHARACTERISTIC CURVES 4-31
6. TYPICAL VACUUM-TUBE CHARACTERISTIC CURVES
The following vacuum-tube characteristic curves were selected as representative of the
triode (type 10), the tetrode (type 865), and the suppressor-grid pentode with normal (type
57) and with remote-cut-off control grid (type 58) . The data were furnished by the RCA
Radiotron Division, RCA Mfg. Co., Inc.
CD 8 °.
iffi
.2 T3
i O
4-32
ELECTRON TUBES
- /u
. L._
pe- 10
je Transfe
cterist cs
5 Volts D.C.
TV
j
/
/
Pf-iar-
t
/
E/=7.
^
7
I
50
r /
1
-
I
7
j( J
-- Z
7 7
7
j 7
I
7 7
r
f
/
40 «
_j y
i
/ / n
Q.
j
E
.55
2 j
^
- I -_^ ,
t
" "1
r r
/
y
-CO
/ 2
7
J2
ijj I
-/
r
j l
J
(f
~l
~^3.
-J
-^ r —
£ v^
T_
- .. . L
Si
^
^
H f
, 1
<r
;7 7
7 ^
1
/
f- r
/ /
'
c? /
J_JL
)
*£*/
f
I
20
/_j
"V7
_ 7 IA_
7
f c
S A
S r
y
/
i
7 ,
^
7
f
/
;
_ _i
JL JL
i i
/
r ""
{__
7
/
V
<?/-
10
7
7 ^
i
/
y
7
7
2 2
r
^
7
Q
^
T
/
? •" ?
2
_j — L^ !
— r- 1
r-
7
L ^t.
/ H7~
-/-
/ I
«r- ^-
_ ^ '
E ^
/
7 ( ~y"
_, _
X -7
rt
SO T-8O —60 —4O
Grid Volts
^20 0"
FIG. 22. Typical Triode (Type 10)
TYPICAL VACUUM-TUBE CHARACTERISTIC CURVES 4-33
2000 400
20 40
Plate MiJIiamperes
FIG. 23. Typical Triode (Type 10)
4-34
ELECTRON TUBES
lype
Average Plate
Characteristics
400
Elate Volts
.800
FIG. 24. Typical Tetrode Characteristics (Type 865)
TYPICAL VACUUM-TUBE CHARACTERISTIC CURVES 4-35
Type - 865
Average
Characteristics
E/»7.5 Volts D..C.
Screen Vo!ts=125 D.C.
22
20
18
1-6
£
14 I
12
-60
0
-50 -40 -30 -20 -10 0 10
Control Grid Volts
FIG. 25. Typical Tetrode Characteristics (Type 865)
4-36
ELECTRON TUBES
Ttoe - 865
Average
Characteristic
Ef=7.5 Volls D.C
Plate Vo ts= 50O C
^
/
-i
/"
-T^l
"3
/
j
f ~
-25
s
~~^i_
f-
7
t
Q
/
-$
f-
oc
JL
d.
J
/i
y-
-/-
(_
J —
*o
^
5f
^
-J--
n
I
T
y
7
/
(
.S
/
t-
7-
1}
-T|
-^
y
- 15
/
/
/
^
;
/
/
^ •
/
/
/
/
/
-^
^
/
/
7
/
- 10
~7~
-^L
7
/-
> -
/
/
7
7
/
Iz
X
- «?
-f*-
__x
^ —
y
—
x
/
r
5
-?^
2
-f
&
o
Tr
Si
S
*fa
re
i
0
p>
I
t _
= —
M
e£
&
= =
••*!
]
W
5C
FIG
£— r
1
)
. 2
6.
?*
^
=
5=
S
T5
=== =
= !=•=:
^
ST
^
=
H
L30-
ISM— ft i i i i iti.. i i i i i i i i i i i i i i i i i i i i
100 150 200
Screen Grid Volts
Apical Tetrode Characteristics (Type 865)
250
TYPICAL VACUUM-TUBE CHARACTERISTIC CURVES 4-37
: i>
4-38
ELECTRON TUBES
Type - 57
Average
Characteristics
E/=2.5 Volts
Screen Volts = 100
Suppressor Volts =0
Plate Volts =250
20'00
16OO
1400
1200 §
1000
40O
200
_,7 —a -5 -4, -3 -.2. -1
CAD.tf.oJ GxLd VStts
FIG. 28. Typical Pentode Characteristics (Sharp Cutoff Type 57)
0
TYPICAL VACUUM-TUBE CHARACTERISTIC CURVES 4-39
2000
1800
1600
1400
I
600
400
200
Average Chi-atracterf sties
S/-2.5 Volts
Screen Voffs* 100
Suppressor Volts=0
Plate volts=250
800
FIG. 29. Typical Pentode Characteristics (Remote Cutoff Type 58)
4-40 ELECTRON TUBES
BIBLIOGRAPHY
Llewellyn, !F. B.t Electron-Inertia Effects, Cambridge University Press, Cambridge (1943).
Ferris, W. R., Input Resistance of Vacuum Tubes as Ultra-high-frequency Amplifiers, Proc. I.R.E.,
Vol. 24, 82 (January 1936).
North, D. OM Analysis of the Effects of Space Charge on Grid Impedance, Proc. I.R.E., Vol. 24, 108
(January 1936).
Strutt, M. J., and A. Van der Ziel, The Causes for the Increase of Admittances of Modern High-
frequency Amplifier Tubes on Short Waves, Proc. I.R.E., Vol. 26, 1011 (August 1938).
Rothe, H., and W. Kleen, Grundlagen and Kennlinien der Electronenrdhren, Akademisehe Verlagsgesell-
schaft, Leipzig (1943). Also by the same authors and publisher, Elecktronenrohren als Anfangsstufen-
Verstarkes (1940).
Langmuir, L, and K. T. Compton, Electrical Discharges in Gases, Part II. Fundamental Phenomena
in Electrical Discharges. Rev. Modern Phys., Vol. 3, 191 (April 1931). This is an excellent paper.
Herold, E. W., The Operation of Frequency Converters and Mixers for Superheterodyne Reception,
Proc. I.R.E., Vol. 30, 84 (February 1942).
Thompson, B. J., D. 0. North, and W. A. Harris, Fluctuations in Space-charge-limited Currents at
Moderately High Frequencies, R.C.A. Rev., Vol. 4, 269-285 (January); Vol. 4, 441-472 (April);
Vol. 5, 106-124 (July); Vol. 5, 240-260 (October 1940); Vol. 5, 371-388 (January 1941).
North, D. O.r and W. R. Ferris, Fluctuations Induced in Vacuum-tube Grids at High Frequencies,
Proc. I.R.E., Vol. 29, 49-50 (February 1941).
Herold, E. W., Superheterodyne Converter System Considerations in Television Receivers, R.C.A. Rev.,
Vol. 4, 324-337 (January 1940). This article gives general expressions for conversion trans conduct-
ance and equivalent noise.
Haller, C. E., Filament and Heater Characteristics, Electronics, July 1944, pp. 126-130.
Ballantine, S., and H. A. Snow, Reduction of Distortion and Cross-talk in Radio Receivers by Means
of Variable-mu Tetrodes, Proc. I.R.E., Vol. 18, 12, pp. 2102-2107 (December 1930).
Herold, E. W., R-f Distortion or Cross-modulation of Pentode Amplifier Tubes. Electronics, April
1940, pp. 82-88.
MAGNETRONS
By W. B. Hebenstreit
In this section only those magnetrons of circular cylinder geometry will be considered.
A cylindrical anode is coaxial to an emitting cathode, and the elements are mounted in a
vacuum envelope. A static magnetic field is parallel, or nearly parallel, to the axis of the
cathode, and a d-c potential applied between the cathode and anode sets up a radial,
static electric field. Under conditions of oscillation, the electrons also interact with an
a-c field.
7. THE NON-OSCILLATING MAGNETRON
The simplest example is the non-oscillating solid anode magnetron. Under the influence
of the electric field, the electron is impelled to move toward the anode. The magnetic
field results in a force on the electron which is normal both to the direction of motion and
to the direction of the magnetic field. Theoretically, there is a minimum critical voltage,
yc, called the cutoff voltage, for each value of the magnetic field, B, for which electrons
will just reach the anode. The formula * for the cutoff voltage is
where e is the electronic charge, m is the electronic mass, ra is the anode radius, and <r is
the ratio of the cathode radius to the anode radius. In this formula it is assumed that the
electrons have zero velocity at the cathode; in addition the relativistic effects, which
become significant at high voltages, are neglected. Since Vc is proportional to Bz, the
locus of eq. (1) for any given geometry is often referred to as the cutoff parabola.
8. THE OSCILLATING MAGNETRON
Principal current interest Hes in the use of a magnetron as a self-excited oscillator. A
convenient classification of oscillating magnetrons can be made by distinguishing among
the several ways in which electrons interact with the a-c fields to sustain oscillations.
For this purpose, three types of interactions can be identified.
Type I. The Negative Resistance Magnetron. If the anode of the magnetron is split
into halves and one half is raised to a higher potential than the other, under certain condi-
tions, most of the electrons will^go to the plate of lower potential. In this event, a negative
* Unless otherwise indicated, mks units will be used in articles 7-9.
THE OSCILLATING MAGNETRON
4-41
resistance exists between the two halves of the anode, and oscillations will be sustained in
a tank circuit which is connected between them.
Type II. The Cyclotron Frequency Magnetron. In the neighborhood of cutoff (see
eq. [1]), the solid anode magnetron will sustain oscillations if the terminals of an L-C tank
circuit are connected between the cathode and anode. The wavelength of the oscillations
which will be sustained is given by
\B = Constant (2)
The most commonly observed value of the constant is about 15,000 centimeter-gausses.
The disadvantage of this type of magnetron is that the electronic efficiency is very low.
ROTATING ANODE
POTENTIAL WAVE
FIG. 1. Approximate Configuration of a Space-charge Cloud of an 8-segment Magnetron Operating
in the 7r-mode
The electrons that initially absorb energy from the field are removed from the interaction
space within approximately one cycle either by striking the anode or by being returned
to the cathode. Those electrons that initially yield energy to the field stay in the interac-
tion space for a longer time. However, after they have lost their energy they begin to
reabsorb it again unless some method is provided for their removal. This is sometimes
done either by tilting the magnetic field slightly with respect to the axis of the cathode or
by installing electrodes at the ends of the interaction space which are made positive with
respect to the cathode. In either method the electrons that have given energy to the r-f
field are drawn off at the ends if the interaction space is short enough.
Type III. The Traveling Wave Magnetron. In this magnetron, the anode consists of
a number of segments. In operation, an r-f standing wave pattern exists in the interaction
space between the cathode and anode. In general, standing wave patterns may be thought
4-42
ELECTRON TUBES
FIG. 2o. Schematic Representation of a Hole and
Slot Magnetron
of as being composed of two waves traveling in opposite directions. The standing wave
pattern in the interaction space is composed of two traveling waves rotating in opposite
directions around the interaction space.
Oscillations are sustained by interaction between one of the traveling-wave components
and the electronic stream. The electronic stream assumes the shape of a spoked cloud
which is centered on the axis of the tube as is indicated schematically in Fig. 1. The
spokes wheel around the interaction space in synchronism with one of the components of
the rotating wave in such a phase that the spokes are in a retarding tangential * electric
field. That is to say that the electrons in the spokes are yielding energy to the r-f field.
Those electrons that come from the cathode in such a phase as initially to absorb energy
from the field are returned to the cathode
after only one orbital loop. Figure 1 shows
the computed paths of electrons emitted
at several different phases. The paths
are drawn as they would appear to an
observer stationed in a system of coordi-
nates which is centered at the axis of the
tube and which is rotating with the same
angular velocity as the rotating wave.
This selective mechanism, that is, the
mechanism by which the unfavorable elec-
trons are rejected by being returned to
the cathode in a relatively short time and
the favorable electrons are grouped into
spokes which stay in a retarding r-f field,
results hi very high electronic efficiencies.
Electronic efficiencies of 60 per cent are
not uncommon.
Associated with the segments of the
anode is a system of resonators. The
resonator system may assume any one of a
variety of forms. One of the commonest
forms is illustrated in Fig. 2a. This figure
is a schematic representation of the hole-
and-slot-type magnetron. Each hole and
slot can be thought of as an L-C tank cir-
cuit with an associated resonant frequency.
In the rising sun structure, illustrated
in Fig. 26, resonators of one resonant fre-
quency alternate with resonators of an-
other frequency. In normal operation,
FIG. 25. Schematic Representation of a Rising Sun *he operating frequency of the ensemble
Anode Block is roughly midway between the resonant
frequencies of the two sets.
From the standpoint of practical application, the traveling-wave magnetron is by far
the most important type of magnetron oscillator. It will be the exclusive concern of article 9,
and, unless explicitly stated, the term ' 'magnetron" will mean a traveling-wave magnetron.
9. OPERATION OF THE TRAVELING-WAVE MAGNETRON
THE R-F PATTERNS OF THE MODES. In a magnetron of TV segments there are
N possible modes of oscillation. The different modes have periodicities of n, where n is
any of the integers 0, 1 , 2, • • • N/2 if N is even, and 0, 1,2, • • • , (N - 1) /2 if N is odd. A
mode number, or designation, is numerically equal to n. Periodicity is here defined to
mean the integral number of repeats of a field pattern in a single revolution around the
anode at any given instant.
The tangential component of the r-f electric field is zero across the face of a segment.
Therefore, the field distribution of a given mode will be the sum of an infinite series of
harmonics. Each harmonic will have a periodicity of k. The only values of k possible are
those for which
k = n - pN (3)
where p is any integer — positive, negative, or zero. If the tube is of the rising-sun variety,
* The type III magnetron is also called the tangential resonance magnetron.
OPERATION OF THE TRAVELING-WAVE MAGNETRON 4-43
m?
?m ??<?? **
II ic— ' '
mf
w w
W
FIG. 3. Field and Potential Distributions of the Modes in an 8-segment Magnetron
4-44
ELECTRON TUBES
where the resonators which connect the segments are alternately large and small, the
allowed values of k will be given by
N
n-p-
(3a)
That is, there will be a set of harmonics associated with each of the two sets of resonators.
The mode for which n = N/2 is sometimes called the TT mode for the reason that adja-
cent segments are 180°, or TT radians, out of phase.
All the modes except the zero mode and the TT mode occur in pairs, or doublets. The
two members of a doublet have the same periodicity although they usually differ in fre-
quency and the patterns are displaced with respect to one another in such a way that a
current loop in the funda-
24 ' ' ' ' ' ' ' mental of one pattern occurs
in the same position as a cur-
rent node in the fundamental
of the pattern of the other.
Some of these principles are
illustrated in Fig. 3 for an
eight-segment tube. For clar-
ity only the electric flux lines
of the fundamental compon-
ent are shown in the inter-
action space. To illustrate
the field configurations in the
resonators, only the magnetic
flux lines are shown. Below
these are plotted the distri-
butions in potential for the
fundamental component. The
reason for the existence of
only one 7r-mode is illustrated
in Fig. 3. The cos 40 solution
corresponds to zero potential
on all the segments.
Although the frequencies of
the several modes are usually
different, all the harmonics
of a given mode are at the
same frequency. Thus, if
/n( = Wn/2-7r) is the operating
frequency of the nth mode,
then the angular velocity of
the pth harmonic of the rotat-
ing wave is un/k, where k is
given by eq. (3) . This point
is stressed for the reason that,
in steady-state operation, the
electronic stream interacts
with only one harmonic of
one mode at any instant.
INPUT CHARACTERISTICS. The d-c voltage for which an electron will just reach
the anode for an infinitesimal r-f voltage on the anode of frequency / and periodicity k is
\
1500.
V
\
\
30%
CONSTANT MAGNETIC FIELD- GAUSS
CONSTANT POWER OUTPUT- KILOWATTS
— - CONSTANT OVERALL EFFICIENCY
TYPICAL OPERATING POINT
FIG. 4.
16 20 24 28
DC CURRENT, I, IN AMPERES
Magnetron Input V-I Characteristic
32
given by
VT
k
27r/m
(4)
Equation (4) defines a threshold voltage. Empirically it is approximately equal to the
operating voltage at low currents although changes in the r-f loading will cause changes in
the input d-c voltage.
For any fixed loading the input voltage varies approximately linearly with input cur-
rent for any fixed value of magnetic field, as is indicated in Fig. 4. Figure 4 shows voltage
plotted as a function of current for various values of magnetic field. In addition to the
constant magnetic field lines, contours of constant efficiency and constant power output
are also shown. A method for obtaining the type of data required for such a V-I char-
acteristic is described in Section 11, Microwave Measurements.
OPERATION OF THE TRAVELING-WAVE MAGNETRON 4-45
Although the performance chart in Fig. 4 is typical, it does not indicate the possible
range of operating characteristics and parameters of magnetrons. Table 1 lists operating
data for five magnetrons. The data for each tube are for some one point on its V-I char-
acteristic. The most striking tiling about the data is the large range of variation of the
several parameters without any apparent correlation. It will be shown in the sequel,
however, that the data do fit into a logical scheme.
Table 1
Example
Wavelength,
centimeters
Voltage,
volts
Current,
amperes
Magnetic
field,
gausses
R-f Power
Output,
Watts
I
II
III
IV
V
1
3
5
10
50
15,000
30,000
2,500
50,000
2,000
15.0
40.0
0,1
200.1
1.0
8,000
8,000
3,000
2,500
800
75,000
500,000
100
4,000,000
1,000
SCALING. If, in the examples in Table 1, all the tubes were assumed to be working
in an equivalent way (for example, all with the same electronic efficiency), then the data
shown, together with the geometrical parameters, would correlate in accordance with the
principles of scaling. The principles of scaling state that in the variation of the parameters,
7, /, B, h, 7*a, and \ where h is the anode length, equivalent operation may be obtained
by maintaining the following three parameters invariant :
VB (5)
In addition, it is assumed that the ratio of cathode radius to anode radius and the number
of segments also are maintained constant.
It would be instructive to consider an example of the type of sealing in which every
linear dimension is scaled by the same factor, S. Let the unprimed quantities represent
the tube from which it is desired to scale, and let the primed quantities represent the tube
to be derived; then
V = SX
ra' = Sra
h' = Sh
From (5), since (X'AO - (XA) and (X'AV) = (X/r«),
V' = V I' = I E' — —
Thus, the new tube will work at the same voltage and current but the new magnetic field
will be l/S times the original magnetic field. This type of scaling is most useful when the
factor S does not differ greatly from unity. Ordinarily it cannot be applied if S is very
large or very small. For example, suppose that X = 30 cm and X' = 3 cm. In this case,
$ — 0.1, and, since I = I' ', the surface current density at the cathode will be up by a
factor of 100 in the new tube. A current density of 10 amp per sq cm in the 30-cm tube
is a quite moderate figure. A current density of 1000 amp per sq cm cannot be attained
with present techniques. In order to scale over such wide ranges, it is usually necessary to
extend the scaling laws to include N and cr. When these parameters are included, the
quantities that must be kept invariant are
/i \
a3) (5a)
where k is used instead of N to emphasize the importance of the field periodicity. In
7r-mode operation k will be JV/2.
Scaling in accordance with the invariants in (5) and at the same time maintaining the
same N and <r gives fairly accurate results. Scaling in accordance with the invariants in
(5a) will give good results in predicting currents, voltages, and magnetic fields. However,
it is usually found that equivalence does not hold for large changes in N or in a: In
particular it is usually found that electronic efficiency decreases with increasing N and
increasing cr.
MODE SEPARATION AND MODING. The frequencies of the several modes are
separated by an amount which depends upon the type and degree of coupling among the
several resonators. Such mode separation is advantageous for the reason that it allows
4-46
ELECTRON TUBES
(CO
(b)
1 r
•
1
, fS
" " SJ "
" 1
I
i
,cz>
ts
I
1
« * „ '• \ 1 .,
r
*. \
SEC. A-A
SHOWING LOCATION
OF STRAPS IN TOP
OF ANODE
Cd>
FIG. 5. Magnetron Anode Strapping Methods, (a) Early British, (6) single ring, (c) echelon, (d) double
ring.
OPERATION OF THE TRAVELING-WAVE MAGNETRON 4-47
the desired mode of operation to be excited independently of the other modes. This
appears to be one of the conditions necessary for high electronic efficiency.
From eq. (3) it might also seem desirable to separate the values of f/k in order that no
two modes have the same threshold voltages. This has appeared to be true in some cases,
but, in general, when taken alone, this condition is an unreliable index of the possibility
of moding. The problem is complicated by several factors including, principally, such
things as relative r-f loading of the modes, the noise levels at the start of oscillations, the
transient behavior of the modulator and power supply, and the instability of the space
charge of the magnetron at high current levels. A complete analysis of moding is beyond
the scope of this article. However, a few general remarks can be made. In these remarks,
it will be assumed that N is even and the 7r-mode operation is desired.
Two distinct types of moding have been observed. One, called the mode skip, occurs
principally in the high- voltage pulse magnetrons. The magnetron fires in both the TT mode
and an unwanted mode. ("Unwanted mode" is to be considered as being denned here so
as to include a non-oscillating state which sometimes occurs.) However, it fires in only
one mode during any one pulse. It alternates between the two modes in more or less
random fashion. This type of moding can usually be cured either by reducing the r-f
loading on the magnetron, by reducing the rate of rise of the applied voltage pulse or by
reducing the applied voltage, or by a combination of the three.
A mode shift, the other type of moding, is encountered chiefly in low-voltage c-w mag-
netrons. It consists of a shift from one mode to another. One of its principal causes is
an inherent instability in the space charge at high current. In general, it can be cured by
reducing the r-f loading or by reducing the operating current. In the pulsed case, a mode
shift is usually observed to occur during a single pulse and is relatively unaffected by
changes in the rate of rise of the applied pulse. If the cathode is well designed, the high
current instability will occur at currents which are lower than those necessary for tempera-
ture limitation. Occasionally, however, mode shifts have been observed which involve
instability due to temperature-limited operation.
METHODS OF MODE SEPARATION. The two most important devices for achiev-
ing frequency separation of the modes involve the use of straps and of the rising-sun
structure.
Figure 5 shows several strapping methods schematically. One of the most widely used
is the double ring strapping of Fig. 5a, in which there is a pair of concentric rings at each
end of the anode. One ring of a pair is connected to one set of alternate segments. The
other ring is connected to the other alternate set of segments. In -rr-mode operation, one
strap or ring is everywhere at the same potential and the two rings at one end are 180°
out of phase. Hence, the straps constitute mainly a capacitance loading of the resonators
with a resultant increase in wavelength in the TT mode over the unstrapped case. In the
n = 1 mode, the potential distribution on a strap is almost sinusoidal and periodic in only
one revolution around the anode. Moreover, the two rings in a set are at nearly the same
potential. Thus, the principal effect of straps in the n — I mode is a shunt inductance so
that the n = 1 mode wavelength will be less in the strapped case than it is in the unstrapped
case. Modes in between the n = 1 and the TT mode will be affected in a way intermediate
between the two extremes first mentioned. That is, as n increases from 1 to TV/2, the
inductance effect of the straps decrease while the capacitive effect increases.
Figure 6 shows the mode spectra of three different types of 18 segment magnetrons.
The spectrum in Fig. 6a is for an unstrapped symmetrical tube, that in Fig. Qb for
a strapped symmetrical tube, while Fig. 6c shows the spectrum for a rising-sun tube.
At wavelengths shorter than 3 cm, the mechanical problem of making strapped mag-
netrons becomes very difficult. The rising-sun structure avoids this difficulty by provid-
ing mode separation without straps. It works on the principle that the normal mode
frequencies of a system of resonators become separated by the introduction of asymmetries.
The mode spectrum of the rising sun is composed of two branches. Each branch is asso-
ciated with one of the two sets of resonators.
OUTPUT COUPLING. The r-f energy can be coupled to the load in several ways. Of
these, two are of major interest: loop coupling and wave-guide coupling. The first type is
indicated schematically in Fig. 2a; the second is shown schematically in Fig. 7. In Fig. 7,
coupling is obtained through a slot in the back of one of the resonators. The quarter-wave
low-impedance transformer section steps down the impedance of the wave guide, which is
of the order of all ew hundred ohms, to the low impedance required at the slot opening,
which is, in somejjiases, as low as 1 or 2 ohms.
The choice bew teen loop output or wave-guide output is usually made on the grounds
of mechanical feMtbility and convenience. At wavelengths greater than 10 cm, r-f trans-
mission is ordinaJMy done in coaxial lines. The size of choke assemblies and window struc-
tures in wave grilles makes them cumbersome and difficult to fabricate. For these rea-
4-48
ELECTRON TUBES
MODE NUMBER,
FIG. 6. Mode Spectra for Three Different Types of IS-segment Magnetrons Having the Same 7r-mode
Wavelength, (a) Unstrapped symmetrical magnetron, (Z>) strapped symmetrical magnetron, (c) rising
sun magnetron.
UNIFORM OUTPUT WAVEGUIDE v
TRANSFORMING
FIG. 7. Illustration of a Method of Wave Guide Output Coupling
OPERATION OF THE TRAVELING-WAVE MAGNETRON 4-49
sons, loop coupling outputs are usually found at the longer wavelengths. Below 10 cm,
wave guides are usually used for transmission, and the physical size of wave-guide outputs
is reduced to manageable proportions.
In common with any self-excited oscillator, the efficiency and frequency stability of a
magnetron depends upon the amount of coupling between the magnetron and the load. In
addition, for any given coupling, the efficiency and frequency stability will change as the
amount of loading is changed. A quantitative measure of the variation of efficiency and
frequency with loading is obtained from a Rieke diagram, an example of which is shown in
Fig. 8. Contours of constant power output and contours of constant frequency are
CONTOURS OF CONSTANT POWER OUTPUT
CONTOURS OF CONSTANT FREQUENCY
FIG. 8. Rieke Diagram
plotted on a polar diagram. Load impedances on a polar diagram may be specified by a
characteristic impedance of the transmission line into which the magnetron is coupled,
together with a reflection coefficient. The modulus of the reflection coefficient is propor-
tional to the distance from the pole of the diagram while its argument is proportional to
the angular displacement around the diagram. The load line characteristic impedance
ZQ, the load impedance Z, and the voltage reflection coefficient r are related by
z - ZQ v*
f - rr , ^ = /^
(6)
where p is the modulus and <j> is the argument of r. The region on the Rieke diagram of
high power and high frequency density is the region of heavy loading. The center of the
diagram corresponds to a matched load; that is, the load impedance is equal to the trans-
mission-line characteristic impedance. Ordinarily, the loading is maintained constant, at
the match point, over the V-I characteristic, as in Fig. 4. On the other hand, the magnetic
field and either the current or voltage is held constant over a Rieke diagram. A descrip-
tion of some of the techniques for obtaining the data for a Rieke diagram and a discussion
of polar diagrams will be found in Section 11, Microwave Measurements.
A quantitative measure of the frequency stability with respect to perturbations in
loading at the match point is the prill ing figure. Pulling figure is defined as the greatest
excursion of frequency observed as the modulus of the reflection coefficient is maintained
constant at a value of 0.2 and its phase angle is varied through 360°. For the example
4-50
ELECTRON TUBES
shown, the pulling figure is about 0.2 per cent of the center frequency. For a magnetron
operating at a wavelength of 3 cm this would represent a pulling figure of 20 Me.
If the coupling from the magnetron to the transmission line is made tighter, the power
output and the pulling figure at the match point will both increase. Nearly all magnetron
output circuits are designed to provide some predetermined compromise of eflSciency and
pulling figure when the tube is operated into a matched line.
TUNING. The frequency of oscillation is determined almost entirely by the geometry
of the cavities, that is, by the equivalent inductance and capacitance of the oscillator tank
circuit. In order to tune the magnetron, it is necessary to change either the inductance
or capacitance or both.
Figure 9 shows three tuning methods schematically. The inductive pin tuning method
is depicted in (a) . An array of copper pins is disposed so that they may be inserted and
r fr
FIG. 9. Methods of Magnetron Tuning, (a) Inductive pin, (6) segment-to-segment capacitance, (c)
strap-to-strap capacitance.
withdrawn from the inductive portion of the resonators. As the pins are inserted, the
effective inductance is decreased and the frequency goes up. Capacitance variation
schemes are shown in Figs. 9& and 9c. In (6), a movable conducting ring changes capaci-
tance between the segments. In (c), the ring changes the capacitance of the straps.
The schemes shown in (a) and (c) are capable of giving tuning ranges of about 20
per cent. The scheme shown in (6) is usually limited to a somewhat shorter tuning
range for the reason that different modes tune at such widely varying rates with
respect to tuner displacement that the TT mode tunes but a relatively short distance before
encountering interference from other modes.
BIBLIOGRAPHY
Collins, G. B. (ed.), Microwave Magnetrons, M.I.T. Radiation Laboratory (sponsor). McGraw-Hill
(1947).
Brainerd, J. G.f et aZ., Ultra-High Frequency Techniques. Van Nostrand (1942).
Fisk, Hagstrum, and Hartman, Bell Sys. Tech. J., Vol. 25, 167 (1946).
Herriger and Hulster, Zeit. /. Hockfrequenz., Vol. 49, 123 (1937).
Kilgore, G. R-, Proc. I.R.B., Vol. 24, 1140 (1936).
Postnumus, K., Wireless Engineer, VoL 12, 126 (1935).
Megaw, E. C. S., J. I.E.E. (London), Vol. 72,326 (1933).
Okabe, K, Proc. I.R.E., VoL 17, 652 (1929).
Hull, A. W., Phys. Rev., Vol. 18, 31 (1921).
Habann, Zeit.f. Hochfrequenz., Vol. 24, 115 and 135 (1924).
Blewett and Ramo, Phys. Reo.t Vol. 57, 635 (1940).
KLYSTRONS (EMPLOYING TRANSIT TIME BUNCHING) 4-51
KLYSTRONS
By A. L. Samuel
Electron tubes which make use of the principle of velocity modulation are now known
as klystrons. The name klystron was originally a registered trademark. It is now applied
to all tubes of the same general type without regard to the manufacturer. A klystron
has been denned by the IRE as an electron tube in which the distinguishing features are
the modulation or periodic variation of the longitudinal velocity of an electron stream
without appreciable variation of its convection current and the subsequent conversion of
this velocity modulation into convection-current modulation by the process of punching.
All commercial tubes of the klystron type make use of cavity resonators, although such
resonators are not, in principle, essential to their operation. Two types of klystrons are
in general use: tubes of the first type bear no further designation: tubes of the second
type are referred to as reflex klystrons or simply reflex tubes.
10. EXYSTRONS (EMPLOYING TRANSIT TIME BUNCHING)
A few typical klystrons are shown in Figs. 1 and 2. As already stated, it is customary,
although not essential, to employ resonant cavities as the tuned circuits associated with
the input and output portions of these amplifiers. These cavi-
ties take the place of conventional circuits and must be tuned
to the operating frequency. They may be partly external to
the tube proper, or they may form an integral part of the tube
as supplied to the user. Cavities are used because they produce
larger effective fields in the interaction gap regions than could
be obtained by any other means.
The basic principles of the klystron amplifier may be ex-
plained by referring to Fig. 3. This figure illustrates a tube
which consists of (1) an electron gun, composed of a heater, a
cathode, and auxiliary focusing electrodes; (2) an input region
called the input gap, defined by two grids which in this case
form a part of a cavity resonator; (3) a conversion region called
the drift space which is relatively free of electric or electro-
magnetic fields; (4) an output region, called the output gap,
again defined by two grids which form a part of a second cavity
resonator; and (5) a collector electrode whose sole function is to
collect the electron stream after it has traversed the working
region of the tube. These five portions of the tube correspond
directly to the five essential operations that must be performed
in any electron tube. The separation of these operations makes
it possible to consider them separately and to explain the opera-
tion of the device in very simple terms. These operations are,
obviously, (1) the production of an electron stream, (2) the
modulation or variation of some property of this stream in ac-
cordance with an input signal, (3) the conversion of the original modulation into a form in
which it can be utilized, (4) the utilization of the stream to produce an output signal, and
(5) the collection of the electron stream.
Referring to Fig. 3, the field in the input gap region of the tube varies the velocity of
the electron stream in a cyclic manner, the variation in velocity being assumed to be small
compared to the average velocity imparted to the stream by the d-c fields. Those electrons
which arrive when the field is in an aiding direction are speeded up; those arriving a half
cycle later are slowed down. The contributions in energy made by the field to some of the
electrons of the stream is nearly balanced by the energy taken from those electrons which
are slowed down. The modulating process, therefore, requires substantially no power,
most of the input power being consumed by ohmic losses in the walls of the input cavity.
All the electrons, except those intercepted by the grids, proceed through the next region
of the tube, the so-called drift space, where the electron stream becomes bunched through
the simple process of the faster electrons, that is, those that are speeded up by the field in
the input gap, overtaking the group of slower electrons that precede them. This bunching
process converts the original velocity modulation into a variation in the rate at which
electrons pass any given point. The stream as it crosses the output gap appears super-
ficially like the stream of electrons in the screen-grid plate region of the conventional space-
la, A Typical Klys-
tuon of the Integral Cavity
Type Shown without Its
Tuner. (The 3K30 oscil-
lator amplifier.)
4-52
ELECTRON TUBES
Coarse Tuning
Adjustment •
Tuning Ring
Clamp
Loading Spring
Coarse
Tuning
Adjustment
Tuner Knob
Loading
Spring
Spreading
Cone Tuner Struts
FIG. 16. The 3K30 Shown in Section with an 11-C Tuner Attached
charge control tetrode. It, therefore, induces currents in the output cavity and delivers
power to the output in just the same way that an electron stream delivers energy to the
field between the screen and the plate of the conventional
tube. The tuning of the output cavity must be adjusted to
cause the maximum value of the field to occur in a retarding
direction at the time that the effective center of an electron
bunch crosses the output gap. Finally, the spent electron
stream is collected by a final electrode where the energy re-
maining in the stream is dissipated as heat. This is to be
contrasted with the ac-
tion in the conventional
tube where the plate
performs the dual func-
tion of providing the
output circuit retarding
field and of dissipating
unused energy as heat.
An interesting possi-
bility exists in the klys-
tron amplifier of utilizing
the electron stream in
cascade to provide either
a multistage amplifieror
a combination function
device such, for example,
as an oscillator buffer
— -^r,— - Collector
•Output Gap
Input
Terminal
Input
Resonator
•Drift Space
Input Gap
'Electron Gun
FIG. 2. The Type 2K47 Klys-
tron. Frequency Multiplier
FIG. 3. A Sectional View of a Klystron
Amplifier
amplifier. When the electron stream traverses the output gap in the simple amplifier, it
obtains an augmented velocity modulation as a result of the higher field intensity existing
in this cavity — this at the same time that the stream delivers energy to the cavity because
of its bunched condition. This augmented modulation is in quadrature with the original
KLYSTRONS (EMPLOYING TRANSIT TIME BUNCHING) 4-53
modulation. At low modulation levels, such as those obtained in an amplifier, it can be
thought of as existing quite independently of the original modulation. In the ordinary
two-cavity single-stage amplifier, no use is made of this added modulation. However, by
providing a second drift space and a third cavity, an additional stage of amplification can
be obtained. The middle cavity or cascade cavity need have no external connection, al-
though, if broad band amplification is desired, it is
necessary to load this cavity in some fashion to reduce
its effective Q to a value comparable to that of the
input and output cavities which are loaded by their
external circuit connections.
The gain of a klystron amplifier varies with the
input signal level in quite a different way from the
behavior of other types of amplifiers. At low levels,
the gain depends only on the beam current, the beam
voltage, and the physical dimensions of the tube.
However, as the drive is increased beyond a certain Input
point, the phenomenon of overbunching sets in and FIG. 4. The Variation in Output Power
the gain begins to decrease. Eventually a maximum *lth tne o4rbu^hmg
output is reached ; with a further increase in the input,
the output actually decreases. This is illustrated in Fig. 4, where the output as a function
of the input is plotted for a typical klystron amplifier.
At low levels, the gain of a klystron amplifier is given by
Gain « ZiZ2Mi*M22Sz (1)
where Zi and Z% are the impedances of the input and output cavities respectively as measured across
the interaction gaps. The parameters Mi and M-i are the absolute values of the input and output
beam coupling coefficients or so-called modulation coefficients and express the effectiveness with which
the fields in the cavities interact with the electron stream. The parameter 5 is the absolute value of
the beam transadmittance and is a measure of the ratio of current variation produced by the bunching
process to the equivalent voltage variation impressed on the beam.
The cavity impedances can be measured directly if desired, or they may be computed from measured
values of the characteristic impedance and Q of the cavity.
The absolute value of the beam coupling coefficient for the gap between two axial cylinders
without grids varies for different electrons depending upon their distance from the axis of the beam.
The value for that portion of the beam lying at a radial distance from the axis of 8p where 6p is expressed
in radians at the operating frequency and with tubes having a radius of Br (also in radians) is given by
^ = !inJ^2).^M (2)
where the Jo's are modified Bessel functions of the first kind.
The absolute value of the beam coupling coefficient for an interaction gap between ideal grids is
given by
where 9g is the electron transit angle of the gap denned as the time required for the unmodulated electron
beam to cross the gap measured in radians at the operating frequency. The value of 6 may be com-
piled from
,
XV?
where X is the gap spacing, X is the free space wavelength corresponding to the operating frequency,
and V is the voltage corresponding to the velocity of the electron beam. The parameters X and X
are measured in the same units (usually centimeters) , and V is in volts.
The absolute value of the beam transadmittance for low signal levels is given by
fl-£' C5)
where 8 is the electron transit angle in the drift space, I is the beam current in amperes, VQ is the
beam voltage, and <r is a reduction factor to account for certain space-charge effects that will not be
discussed. In well-designed amplifiers, the parameter <r is usually of the order of 0.5 at the recommended
operating conditions and increases to 1.0 as the beam current (at a given voltage) is decreased to a
low value.
At high levels the beam trans conductance is sometimes expressed as
where V is the value in volts of the velocity modulation impressed on the beam, and */i is a Bessel
function of the first kind.
This expression is based on kinematic considerations only and neglects space charge and other
sources of non-linearity. It may be used as a rough basis for predicting the general behavior of a,
klystron amplifier for large signals, but it does not agree quantitatively with experimental results.
4-54
ELECTRON TUBES
11. REFLEX KLYSTRONS
A reflex tube or reflex klystron is a special form of the klystron oscillator employing a
single cavity with, a single interaction gap to perform the functions of both the input and
output circuits (see Figs. 5 and 6). The
electron stream is velocity modulated on a
first transit of this gap and is forced to
cross the gap a second time by means of a
repelling or reflecting field. The electrons
become bunched in the process of reflection,
the speeded-up electrons penetrating the
field to a great distance and therefore
taking longer to return than the slowed-
down electrons in just the same way that
a ball thrown upward in the earth's gravi-
tational field takes longer to return if
thrown with high velocity than if thrown
with low velocity. In order for the oscilla-
tions to be self-sustained, the returning
bunches of electrons must arrive at the
interaction gap at the correct phase of the
alternating field, that is, when the field has
its maximum value in the retarding direc-
tion. This requires that the electrons re-
main in the reflecting field region for a
critically valued length of time, a time
FIG. 5. The 707A Reflex Klystron Em-
External Cavity, Shown with the Ca- '
Disassembled
nploying t._
that is approximately n H- 3/4 cycles at
the operating frequency, where n is any
integer equal to or greater than zero. This time can be adjusted by varying the velocity
of the beam as it crosses the gap on the first transit or, more usually, by varying the
voltage of the repeller. As the voltage of the repeller is varied, a series of operating regions
Resonator.
CoopJIpg Loo|
Flexible Diaphragm
Tuner S'cre'w.-
Accelerating Grid-
Tuner Bow-
Tuner Back Strut
Repeller
•Cavfty Grfds
Beam Forming
Electrode
Cathode
Cathode Heater
Coaxial Output Lead-
FIG. 6. The 2K25 Reflex Klystron, a Mechanically Tuned Tube of the Integral Cavity Type
called modes will be observed corresponding to different values of n in the above relation-
ship. Only a limited number of modes corresponding to values of n from 1 or 2 to 4 or 5
are actually observed, and usually only one or two of these modes produce enough power
to be useful. I'he variation in the output power for a typical reflex tube is shown in Fig. 7.
It will be observed that oscillations are actually produced for a limited range in voltage
in the vicinity of the optimum values, and that a variation of frequency occurs as shown
by the top curves. This variation in frequency with voltage is called electronic tuning.
REFLEX KLYSTRONS
4-55
Electronic tuning is often employed as a means for critically adjusting the operating
frequency in applications where the accompanying variations in the output power can be
tolerated, such, for example, as a local
oscillator in a superheterodyne receiver.
Electronic tuning finds its greatest useful-
ness in connection with automatic fre-
quency control circuits. Since the mode
with the highest output has the smallest
electronic tuning band width, a compromise
must often be made between output and
tuning range. The electronic tuning range
is generally small as compared to the usual
mechanical tuning range. When electronic
tuning is employed, it is essential that the
mechanical tuning be adjusted so that the
operating point falls somewhere near the
middle of the electronic tuning range where -700 -soo —soo —400 -300 -200 -100
the frequency can be shifted a reasonable Reflector Voltage
amount in either direction with the elec- FIG. 7. A Typical Mode Curve for a Reflex Elys-
tronic control without too much cha^e in
output power. Electronic tuning and other
associated phenomena can be explained by
considering the way in which the impedance of the electron stream as seen by the cavity
varies with the electron transit time in the repeller region.
Figure 8 is a plot of the small signal beam conductance showing the relationship
1
i
-f-20 °
\
J.1Q ag
N
\
\
o '8-
\
\
\
\
V
\
si
Be
im
vol
12
50
i
en
<v
DltS
ge
-
40
~30U*
1
f \
Fr«
qu<
nc
ft
4c)
92
50
80=~
1
i
/•
00^
1
\
/
60 0 =
I
\
/
A
1
1
f
/\
o •*
the 2K41 Tube)
=
*
(VM6/2V0')
2V Q VM6/Vo
(7)
Negative of
Circuit Admittance
Small Signal Admittance
of Electron Stream.
where the first term represents the magnitude of small signal admittance, and the last term is the
phase angle. Here 0 is the transit angle in the repeller region, and the rest of the symbols have the
same significance as in the article
on klystrons employing transit
time bunching. The second term
accounts for the decrease in mag-
nitude of the conductance which
occurs for large signal levels and
is similar to the compression term
appearing in the expression for
the small signal transadmittance
of the klystron amplifier. The
final term gives the phase angle
of the conductance.
If the real part of this admit-
tance is negative and larger in
magnitude than the positive real
component of the cavity admit-
tance, oscillations will build up
until limited by the non-linearity
given by the second term. Under
stable operating conditions, the
relationship
Yg + Ye _ 0 (8)
must be satisfied, where Yc is the
admittance of the cavity. The
cavity may be assumed to behave
as a simple shunt tuned circuit
in the vicinity of the resonant
frequency so that
FIG. 8. The Admittance of the Electron Stream as Viewed from the . / .
Cavity for a Reflex Klystron. Oscillations can occur only in the re- yc = G + — I -- ! — - 1 (9)
gion where the negative conductance of the beam exceeds the pos- QQ VWQ w /
itive conductance of the circuit.
Typical Point at which
Oscillations may Start,
ance, QQ is the cavity Q, «Q is the angular frequency at resonance, and a is the angular frequency cor-
responding to the particular value of Yc. The negative of this value is plotted in Fig. 8 and appears
as the straight line to the left of the imaginary axis.
Oscillations will not be sustained for all values of Yg lying in the shaded area on the figure. For values
of Yg lying to the left of the Yc line, oscillations will build up until Yg sinks along a radial line arriving
at a stable operating point on this line. If the operating point lies on the real axis, the oscillations vriH
occur at the resonant frequency of the cavity. Operating points off the axis correspond to oscula-
tions at a frequency which differs from the resonant frequency by a sufficient amount to* provide
4-56
ELECTRON TUBES
the necessary reaction component of admittance specified by the operating point. This effect is called
electronic tuning.
The output impedance characteristic of a reflex tube can best be illustrated by plotting
this characteristic on the reflection qoefficient plane (sometimes called a Rieke diagram on
a Smith chart) . A typical plot is shown in Fig. 9, where lines for constant power are shown
solid and lines for constant frequency are plotted on a background of orthogonal circles
representing fixed values of the resistive and reactive components of the load impedance.
The region on the plot where the constant-frequency lines tend to converge is called the
ERes<= 300 Volts
FIG. 9. The Variation in Output Power and Frequency with the Load Impedance for a Typical Reflex
Klystron (the 2K25) Shown on the Reflection Coefficient Plane
frequency "sink," and the minimum amplitude of standing wave ratio that will cause the
tube to operate in this region of discontinuity is called the "sink margin." It is customary
to require a sink margin of 8 db. A second important characteristic is the so-called pulling
figure which is defined as the maximum difference in frequency produced when a mismatch,
having a reflection coefficient of 0.2 as measured at the prescribed output coupler, is
varied through 360°. The pulling figure for the tube shown in Fig. 9 is approximately 4 Me.
The power output, electronic tuning sink margin, and pulling figure for the typical reflex
tube will be found to vary somewhat over the mechanical or thermal tuning range of the
tube. Curves showing these variations for any particular tube are customarily supplied
in the technical information sheets published by the manufacturers,
The coarse adjustment of frequency is usually made by mechanical means, either by
varying the effective size of the external portion of the cavity or by internal changes,
usually of the length of the interaction gap, and hence of the effective capacitance loading
of the cavity. In most tubes where capacitance tuning is employed, the necessary motion
is transmitted through the vacuum envelope by means of a flexible diaphragm. Recently,
a number of tubes have been introduced in which mechanical cavity tuning is produced
TUBE TYPES
4-57
internally by thermal expansion means. This method, called thermal tuning, makes it
possible to adjust the frequency of the tube over its entire mechanical tuning range by
electrical means, without the large variations in output power that are encountered with
electronic tuning. The thermal tuning speed is limited by the thermal capacity of the
tuning mechanism, but it is sufficiently fast for many automatic frequency control appli-
cations.
12. TUBE TYPES
Many of the tubes listed in Table 1 were made for the armed services during World
War II, and some may not be commercially available. The prospective user should con-
sult the manufacturer in regard to their availability and should follow his recommenda-
tions regarding operating conditions and ratings. The data of Table 1 are indicative of
typical operating conditions and are supplied for general reference purposes only.
Table 1. Western Electric Reflex Tubes — External Cavity Type
Number
Frequency,
megacycles
Reso-
nator
Volt-
age
Reflector
Voltage
(Negative)
Heater
Volt-
age
Out-
put,
milli-
watts
Tuning Range,
megacycles
Remarks
Mechani-
cal
Elec-
tronic
Ther-
mal
707A/B
2K48
2,500- 3,750
3,000-10,000
300
1,000
0- 275
0- 500
6.3
6.3
70
24
*
35
10
Table 1 — Continued. Western Electric Reflex Tubes — Internal Cavity Type
7260
726B
726A
2K29
2K56
2K54
2K23
2K55
2K22
2K26
2K25
2K45
723A/B
2K50
2,700- 2,930
2,880- 3,170
3,170- 3,410
3,400- 3,960
3,840- 4,460
4,290- 4,560
4,275- 4,875
4,590- 4,860
4,240- 4,910
6,250- 7,060
8,500- 9,660
8,500- 9,660
8,700- 9,550
23,215-24,750
300
300
300
300
300
1,130
1,130
1,130
300
300
300
300
300
300
50- 210
50- 210
50- 210
50- 210
125- 175
800-1,100
600- 900
625- 850
75- 235
70- 150
75- 200
95- 145
90- 200
20- 130
6.3
6.3
6.3
6.3
6.3
6.3
6.3
6.3
6.3
6.3
6.3
6.3
6.3
6.3
120
120
120
95
65
700 t
250 f
700 t
85
50
30
30
25
10
230
290
240
560
620
270
600
270
670
810
1,160
25
25
25
32
30
Pulsed
Pulsed
Puked
8 sec tuning time
2 sec tuning time
35
35
32
50
32
65
1,160
935
850
The data above were obtained on tubes manufactured for the Army and Navy.
Table 1 — Continued. Raytheon Manufacturing Company
T?aon
Out-
Tuning Range,
Type
Frequency,
megacycles
iteso-
nator
Volt-
Reflector
Voltage
(Negative)
Heater
Volt-
age
put
Power,
milli-
megacycles
Remarks
Mechan-
Elec-
Ther-
age
watts
ical
tronic
mal
QK269
1,200- 1,500
300
100-220
6.3
150
300
12
707B
3,400- 3,600*
300
155-290
6.3
150
20
Requires external
cavity
2K28
3,400- 3,600*
300
155-290
6.3
150
20
Requires external
cavity
QK159
2,950- 3,250
300
112-250
6.3
150
20
5721
4,290- 8,340*
1000
60-600
6.3
160
12
Requires external
(min.)
cavity
2K25/723A-B
8,500- 9,660
300
85-200
6.3
33
1160
40
2K33
23,710-24,290
1800
80-220
6.3
40
580
40
Table 1 — Continued. Sylvania Electric Products, Inc.
6BL6
1,600- 5,500*
350
15-700
6.3
125
10
Requires external
cavity
6BM6
500-3,000*
350
15-700
6.3
60
13.4
Requires external
cavity
* Tuning range of external cavity tubes depends upon cavity design and may be anything up to the total range of
the tube.
f Average power based on 0.1 duty.
4-58
ELECTRON TUBES
Table 1 — Continued. Sperry Gyroscope Company — Reflex Klystrons
Type
Frequency,
Resonator
Vn1+«aer«
Reflector
Voltage
Heater
Grid
Vnl+au'p
Output
Tuning Range,
megacycles
(Negative)
Mechanical
Electronic
3K27
750- 960
,000
0-1,500
6.3
+20 to -200
I w
210
10
3K23
950- 1,150
,000
0-1,500
6.3
+20 to -200
1 w
200
10
2K41
2,660- 3,310
,250
0- 750
6.3
+50 to -200
250 mw
650
17
2K42
3,300- 4,200
,250
0- 750
6.3
+30 to -200
250 mw
900
15
2K43
4,200- 5,700
,250
0- 750
6.3
+30 to -200
250 mw
1,500
15
2K44
5,700- 7,500
,250
0- 750
6.3
+30 to -200
250 mw
1,800
15
2K39
7,500-10,300
,250
0- 750
6.3
+30 to -200
250 mw
2,800
44
Table 1 — Continued. Sperry Gyroscope Company — 2-cavity Oscillator/ Amplifiers
Type
Frequency,
megacycles
Reso-
nator
Volt-
age
Grid
Voltage
Heater
Volt-
age
Output
Tuning Range, megacycles
Remarks
Mechanical
Elec-
tronic
3K2I
3K30/
410R
3K22
2,300- 2,725
2,700- 3,300
3,300- 4,000
3,000
3,000
3,000
0 — 200
0 — 200
0 — 200
6.3
6.3
6.3
20w
20w
20w
425 Me
600 Me
700 Me
10 Me
10 Me
10 Me
10-14 db gain
Table 1 — Continued. Sperry Gyroscope Special-purpose Tubes
2K35
2 730- 3 330
3 000
0 — 200
6.3
25w
600 Me
3-cavity, 2-stage cas-
2K34
2K47
2,730- 3,330
/ 250- 280 \
3,000
1 000
0 — 200
0 — 200
6.3
6 3
16w
125 mw
600 Me
Input 30 Me
cade amplifier, 30 to
33 db gain
3-cavity oscillator
buffer amplifier
2-cavity frequency
-2K46 "
V2.250- 3,360 J
(I 730- 3 330 \
1,500
0 — 200
6.3
10-70mw
Output 110 Me
Input 600 Me
multiplier
3-cavity amplifier-fre-
V.8, 190-10,000^
Output 1,810
Me
quency multiplier
GASEOUS CONDUCTION TUBES
By D, S. Peck
For definitions of gas tube, anode, cathode, etc., see pp. 4-03 to 4-06.
Arc. An arc is a discharge of electricity through a gas, characterized by a change in
space potential in the immediate vicinity of the cathode which is approximately equal to
the ionizing potential of the gas. (Proposed for Standards for Pool-cathode Mercury Arc
Power Converters, AIEE.)
13. GASEOUS CONDUCTION
Gaseous discharges may be classified in two groups according to the mechanisms for
producing ionization. The first group, "self-sustaining discharges," includes those in
which the energy for maintaining the discharge is supplied directly by the discharge.
The other group includes those that require some auxiliary power in addition to the energy
of the discharge itself.
SELF-SUSTAINING DISCHARGES. One of the earliest known gaseous-discharge
devices, the Crookes tube, is a typical example of a self-sustaining discharge. In that
tube, cylindrical in form and containing a low gas pressure, a luminous discharge takes
GASEOUS CONDUCTION
4-59
place if potential of sufficient value is applied between two electrodes. The appearance
of the glow is shown diagrammatically with the corresponding voltage distribution in
Fig. I-
It will be observed that immediately adjacent to the cathode is the Crookes, or cathode,
dark space. Across this space a large part of the total tube drop is concentrated. This
drop is such that ions moving toward
the cathode obtain sufficient energy to
remove electrons from the cathode by
bombardment and hence maintain ioni-
zation in the tube.
Following the cathode dark space is a
luminous region, called the negative
glow, in which some of the excited
atoms are returning to normal, radiat-
ing energy in the form of light.
Following the negative glow is an-
other dark space called the Faraday
dark space, then another luminous por-
tion called the positive column which
extends to the anode.
This general type of discharge is used
for the production of light in many neon
and argon signs. It is also employed in
protective tubes and in glow tubes used
for voltage regulation, as well as in cold-
cathode relay tubes.
Another form of self-sustaining dis-
charge is found in tubes employing a
pool cathode. Here the current densi-
ties run much higher than in a glow
discharge, and the cathode dark space
becomes very small so that extremely
high gradients are present close to the
emitting "spot." It is thus possible to
release electrons without the high drop
generally found in so-called glow dis-
charge tubes similar to the Crookes
tube. With a pool cathode, emission
Distance
TIG. 1. Voltage and Glow Diistrbution in Glow Dis-
charge
appears to be true field emission caused by voltage gradient, and not thermal emission
caused by the high temperature of the spot.
DISCHARGES REQUIRING AUXILIARY ENERGY. One of the commonest forms
of this type of discharge is the hot-cathode tube. Here a heated filament or cathode, by
virtue of the thermal energy imparted to the surface molecules, is able to release electrons.
These electrons are drawn from the cathode by the anode field and after sufficient travel
acquire enough energy to ionize the gas atoms by collision. The discharge is very similar
in structure to the glow discharge from a cold cathode, except that the region of cathode
fall is very much smaller and has a lower voltage drop since the electrons are actually
ejected by the emitting properties of the cathode.
Other sources of ionization are possible, such as heat, photoelectrons, and radiation,
CONTROL OF THE DISCHARGE. If, in a simple tube with a cathode and an anode,
a third element known as a grid is introduced between cathode and anode, it is possible to
control the starting of the discharge. If the grid is made sufficiently negative with respect
to the cathode, it produces a retarding field at the cathode in spite of the positive anode
potential and most of the electrons emitted from the cathode are turned back without
receiving sufficient energy to cause ionization. If the grid is then gradually made less
negative, a critical voltage is reached where some electrons acquire enough velocity to
ionize the gas. Within a few microseconds the ionization builds up until the current is
limited only by the impedance of the external circuit.
Once ionization is complete, further changes in grid voltage have little effect on the
discharge in most practical cases. If the grid is made negative, positive ions from the dis-
charge will move toward it, causing a grid current to flow and blanketing the grid suffi-
ciently to prevent its having any further effect on the arc. The grid becomes "sheathed"
with positive ions, the thickness of the sheath depending upon the density of ionization
and, to some extent, upon the grid voltage. The sheath thickness may be of the order of
hundredths or thousandths of a centimeter under normal operating conditions. Only by
4-60
ELECTRON TUBES
using grids with very small openings and relatively large negative voltages is it possible
to make the sheaths large enough to overlap and extinguish the discharge. If, however,
the discharge ceases, as it would when alternating potential is used for the anode supply,
the ionization diminishes to a low value or disappears in a relatively short period of time,
and the grid may again exercise its control function.
VACUUM-TUBE CONTROL VS. GAS-DISCHARGE CONTROL. The character-
istic of a grid-controlled gaseous-discharge tube of passing either no current or full current,
together with the normal inability of the grid to stop the discharge, are two important
differences from hard-vacuum grid-controlled tubes. Although both types possess the
unidirectional conduction properties of a rectifier, the hard-vacuum tube with its con-
tinuous control may be likened to a rheostat in series with a circuit, whereas the gas-filled
control tube may be considered similar to a switch which can be closed at any time but
opened only when current is not flowing. Obviously, the hard-vacuum tube, which func-
tions like a rheostat, must be capable of dissipating the power losses caused by pasage of
current through the tube when the voltage across the tube is increased. The low voltage
drop (from about 5 to 15 volts in most hot-cathode tubes) existing when the gas tube is
passing current results in relatively low losses in the tube, and there is no plate dissipation
whatever when the tube is turned off. Thus, a gas tube is capable of handling much
heavier currents and more power than a hard-vacuum tube of the same size.
Because of the difference in control characteristic the circuit technique used with gas
tubes is entirely different from that employed with hard-vacuum tubes. For instance,
the gas tube may be used as a sensitive relay to operate a contactor when the grid voltage
of the tube reaches a given value. With a voltage of adjustable phase relation on the
grids it may be used as a controlled rectifier tube to control average output voltage. The
gas tube may also be used in suitable circuits to change direct current to alternating cur-
rent or alternating current of one frequency to alternating current of a different frequency.
14. THYRATRON TUBES
A thyratron is a hot-cathode, gas-discharge tube in which one or more electrodes are
employed to control electrostatically the starting of the unidirectional current flow. (IRE
Standard.)
These types of tubes cover an intermediate power range. Tubes are available in sizes
up to 12.5 amp average current and up to 15,000 volts peak. (See Table 1.)
Similar gas tubes are built without grids for use as rectifiers. Since their major single
application is in transmitting circuits, they are listed in article 13 with transmitter tubes.
CONSTRUCTION. Figure 2 shows a typical construction of a simple filamentary-
type gas tube. The filament is in the form of a ribbon of nickel or nickel-cobalt alloy,
formed in a helical or S-shaped form, and
coated with an electron-emissive coating. A
grid in the form of a cylinder is mounted as
shown, and supported by a clamp from the
lower stem. The grid may also be mounted
on the stem leads and supported additionally
from the glass at the top of the tube. The
nickel anode in the form of a cup is mounted
by means of another glass stem at the top. A
washerlike cross piece in the grid determines
the control characteristic by its relative spac-
ing between cathode and anode and by the
size and shape of a hole in the washer. The
sides of the grid shield the control area from
effects of charges collected on the glass walls
and from extraneous fields. Carbonized nickel
is frequently used for these parts because of its
heat-radiating properties, but bright nickel is
PIG. 3. Shield-grid Type sometimes necessary in inert-gas-filled tubes.
FIG. 2. Filamen-
tary-type Thyra-
tron Tube
of Thyratron Tube ' Argon, xenon, and mercury vapor are the
most common mediums for gas tubes.
FOUR-ELECTRODE CONSTRUCTION. Figure 3 shows a sketch of a shield-grid
type of construction. The large shield grid, generally held at a fixed potential, permits
the use of a small control grid of extremely high effective input resistance. The shield
grid shields the control grid from the heat of the cathode and anode and minimizes the
possibility of sputtered or evaporated material from the cathode contaminating the grid,
THYKATRON TUBES
4-61
Table 1. Available Types of Thyratrons
Type
Designation
Anode Current
Peak Anode
Voltage
Cathode
/ = filament
k = heater
loniz-
able
Me-
dium
Remarks
Aver-
age
Peak
Averag-
ing
Time,
seconds
For-
ward
In-
verse
Volt-
age
Cur-
rent
2C4
S
0.005
0.020
30
450
450
2.5k
0.65
Gas
Negative control tube
297A
WE
0.010
0.060
250
250
1.75/
0.35
Gas
>Jpcr<}-f-?VP f»nnfpn1 fnKp
546
GL-
0.020
0.100
15
500
500
6.3k
0.15
Gas
Shield grid tube
269A
WE
0.020
0.20
275
275
2.2f
0.55
Gas
6D4
S
0.025
0.100
30
450
450
Gas
Miniature negative
control tube
233A
RX-
0.025
1.5
,500
1,500
2.5f
2.5
Gas
"NTpo^itivp nf If iKp
629
WL-
0.040
0.2
10
350
350
2.5k
Gas
Negative control tube
2051
Ray, Ch,
0.075
0.375
30
350
700
6.3h
0^6
Gas
Shield grid tube
GL-, RCA
884
RX-, Ch, S,
0.075
0.30
30
350
350
6.3h
0.6
Gas
Sweep-circuit tube
WL-,
RCA, GL-
885
RX-, Ch, S,
0.075
0.30
30
350
350
2.5h
1.5
Gas
Sweep-circuit tube
RCA,
GL-, WL-
610
KU-
0.10
0.40
10
500
500
2.5f
6.5
Gas
Positive control tube
636
KU-
0.10
0.40
15
350
350
2.5f
7.5
Gas
Negative control tube
2D21
RCA
0.10
0.50
30
650
1,300
6.3A
0.6
Gas
Shield-grid tube
338A
WE
0.10
0.60
325
325
10. Oh
0.50
Gas
Negative control tube
2050
Ray, GL-,
0.10
1.00
30
650
1,300
0.60
Gas
Shield-grid tube
Ch, WL-,
RCA
502A
GL-.WL-
0.10
1.0
30
650
1,300
6.3A
0.60
Gas
Shield-grid tube
2A4G
S, Ch, Ray
0.10
1.25
45
200
200
2.5/
2.5
Gas
Negative control tube
178 A
FG-
0.125
0.50
15
500
500
2.5/
2.25
Gas
Negative control tube
17
FG-, WL-
0.50
2.0
15
2,500
5,000
2.5/
5.0
Hg
Negative control tube
967
UE-
0.50
2.0
15
2,500
2,500
2.5/
5.0
Hg
Negative control tube
81A
FG-, WL-
0.50
2.0
15
500
500
2.5/
5.0
Gas
Negative control tube
98A
FG-
0.50
2.0
15
500
500
2.5/
5.0
Gas
Shield-grid tube
97
FG-
0.50
2.0
15
1,000
1,000
2.5/
5.0
Hg
Shield-grid tube
627
WL-, GL-
0.64
2.5
30
1,250
2,500
2.5/
6.0
Hg
Negative control tube
394A
WE
0.64
2.5
5 '
1,250
1,250
2.5/
3.25
Hg and
Negative control tube
gas
3D22
RCA
0.75
6.0
30
650
1,300
6.3A
2.6
Gas
Shield-grid tube
GIB
EL-
.0
8.0
450
700
2.5/
6.3
Gas
Negative control tube
303
CE-
.0
8.0
450
700
2.5/
6.0
Gas
Negative control tube
302
CE-
4^5
1,000
1,000
2.5/
7.0
Hg
Negative control tube
287A
WE
.5
6.0
5
500
500
2.5/
7.0
Hg
Negative control tube
323A
WE
.5
6.0
5
500
500
2.5/
7.0
Hgand
Negative control tube
gas
393A
GL-, WE
1.5
6.0
5
1,250
1,250
2.5/
7.0
Hgand
Negative control tube
gas
3C23
GL-.WL-
1.5
6.0
5
1,250
1,250
2-5/
7.0
Hg and
Negative control tube
gas
678
WL-, GL-
1.6
6.0
1 cycle
15,000
15,000
5.0A
7.5
Hg
Negative control tube
21
KY-
3.0
11,000
2.5/
10.0
Hg
Transmitter keying
tube
628
KTJ-
2.0
8.0
30
1,250
2,500
5.0/
11.5
Hg
Negative control tube
305
CE-
2.0
12.0
850
,700
2.5/
6.5
Gas
Negative control tube
27A
FG-
2.5
10.0
15
1,000
,000
5.0/
4.5
Hg
Negative control tube
973
UE-
2.5
10.0
15
3,000
,000
5-0/
6.75
Hg
Negative control tube
154
FG-
2.5
10.0
15
500
500
5.0/
7.0
Gas
Shield-grid tube
33
FG-, WL-
2.5
15.0
15
,000
,000
5.0A
4.5
Hg
Negative control tube
57
FG-, WL-
2.5
15.0
15
,000
,000
5.0h
4.5
Hg
Negative control tube
67
FG-
2.5
15.0
15
,000
,000
5.0h
4.5
Hg
Inverter tube
95
FG-
2.5
15.0
15
,000
,000
5.0k
4.5
Hg
Shield-grid tube
672
WL-.GL-
2.5
30.0
15
,500
,500
5.0k
6.0
Hg
Shield-grid tube
C3J
EL-
2.5
30.0
750
,250
2.5f
9.0
Gas
Negative control tube
632-A
WL-
2.5
30.0
15
1,500
,500
5.0k
6.0
Hg
Shield-grid tube
677
WL-
4.0
15.0
15
10,000
10,000
5.0k
10.0
Hg
Negative control tube
354A
WE
4.0
16.0
15
1,500
1,500
2.5f
16.0
Hg
Negative control tube
355A
WE
4.0 '
16.0
15
350
350
2.5f
16.0
Hgand
Negative control tube
gas
4-62
ELECTRON TUBES
Table 1. Available Types of Thyratrons — Continued
Type
Designation
Anode Current
Peak Anode
Voltage
Cathode
/ = filament
h = heater
loniz-
able
Me-
dium
Remarks
Aver-
age
Peak
Averag-
ing
Time,
seconds
For-
ward
In-
verse
Volt-
age
Cur-
rent
105
172
676
C6J
306
C6C
624
C16J
41
414
Ch, WI^,
FO-
WL-, FG-
KTJ-
EL-
CE-
EL-
Wlr
EL-
WL-, FG-
GL-.WL-
6.4
6.4
6.4
6.4
6.4
6.4
6.4
12
12.5
12.5
40.0
40.0
40.0
77.0
77. 0
77. 0
77.0
100.0
75.0
100.0
15
15
15
2,500
2,000
2,500
750
750
2,000
2,500
750
10,000
2,000
2,500
2,000
2,500
1,250
1,250
4,000
2,500
1,250
10,000
2,000
5.0/i
5.0A
5.0A
2.5/
2.5/
2.5/
5.0/i
2.5/
5.0/1
5.0A
10.0
10.0
10.0
21.0
18.0
24.0
10.0
31.0
20.0
20.0
Hg
Hg
Hg
Gas
Gas
Gas
Hg
Gas
Hg
Hg
Shield-grid tube
Shield-grid tube
Negative control tube
Negative control tube
Negative control tube
Negative control tube
Negative control tube
Negative control tube
Inverter tube
Metal negative con-
trol tube
15
30
30
NOTES
Prefix Used ly
GL- General Electric Company
FG- General Electric Company
WL- Westinghouse Electric Corporation
KU- Westinghouse Electric Corporation
KY- Eimac
TIE- United Electronics
EL- Electrons, Inc.
Prefix Used ly
CE- Continental Electric Company
RX- Raytheon
Letter Indicates
S Sylvania Electric Products, Inc.
Ch Chatham Electronics
Ray Raytheon
WE Western Electric Company
RCA Radio Corporation of America
•with consequent reduction in grid emission. The shield grid may act also as an electro-
static shield to prevent sudden voltage fluctuations of the anode from inducing transient
voltages on the grid with consequent loss of control. Of course, it is also possible to use
tubes of this shield-grid type with "signal'* voltages on both electrodes so that operation
of the tube is a function of both grid potentials.
METAL TUBES. Metal envelopes are used for many industrial tubes, particularly in
the larger sizes, because of the greater sturdiness and dependability of metal than of glass
and to facilitate mounting the tubes on a panel. In the medium or smaller sizes this con-
struction frequently has no real advantage over glass tubes because internal tube elements
may be as subject to breakage as the envelope under conditions of shock or vibration.
15. VOLTAGE LIMITS OF THYRATRONS
PEAK INVERSE ANODE VOLTAGE. Peak inverse anode voltage is the maximum
instantaneous anode voltage in the direction opposite to that in which the tube is designed
to pass current. (IRE Standards on Electronics, 1938.)
The maximum peak inverse voltage which can be applied is a function of the shape and
spacing of the electrodes, the current conducted, and the gas pressure. In thyratrons
having argon or xenon or some other inert gas, the arcback potential is relatively inde-
pendent of the tube temperature. In mercury-vapor tubes, however, the mercury-vapor
pressure doubles roughly with every 10 deg cent increase so that the maximum peak in-
verse voltage is seriously affected. Figure 4 shows a typical curve of arcback voltage vs.
temperature for a mercury-vapor tube. In rating a tube of this class, therefore, it is
necessary to specify not only the peak inverse voltage but the maximum condensed-
mercury temperature as well.
In designing a tube for high-voltage operation, it is sometimes necessary to constrict
completely the space at the back, or top, of the anode, so that it is impossible for any
discharge to take place between the anode and cathode around the outside of the grid.
PEAK FORWARD VOLTAGE. Peak forward voltage is the maximum instantaneous
anode voltage in the direction in which the tube is designed to pass current. (IRE Stand-
CURRENT LIMITS OF THTRATRONS
4-63
CO
O
o
o
rs
Oi
O
o
o
-4000
nod
M
0
8
Itage
.Tern i
ards on Electronics, 1938.) The same
factors of tube geometry and current
affect the maximum permissible peak
forward voltage. In addition the grid
must be so designed as to maintain
the proper characteristics up to the
voltage desired.
TESTS. The peak forward voltage
may be tested by measuring the con-
trol characteristic at the maximum
temperature ratings, although a com-
mon test is a full-load operation of the
tubes in a circuit giving both peak
inverse and peak forward voltages.
This operation continues at the rated
average current of the tubes for a
length of time sufficient to stabilize
the tube temperature, at which time v 40 50 60 70
the grid control is checked. Thejfre--, , ^ ,.. ®°nderise^8 Temperature
quency of arcback is also observed. 3^££^
The severity of the test varies con-
siderably with the current and voltage conditions at the time of current commutation
from one tube to the next; therefore the type of operation circuit used is important.
When simple circuits are used the voltage is frequently set above the rating to make the
test sufficiently severe.
16. CURRENT LIMITS OP THYRATRONS
Most commercial tubes have cathodes made by coating a base metal such as nickel or a
nickel alloy with one of two types of coatings. The first is barium oxide or a mixture of
barium, strontium, and calcium oxides, formed by coating with the carbonates and reduc-
ing to the oxides by high temperature during the processing. The second is a molecular
mixture of barium oxide and nickel oxide known as barium nickelate, formed by coating
with barium carbonate and a nickel oxide before processing.
Cathode construction is of two general types, the filamentary and the indirectly heated.
The filamentary type is simple in construction and has a relatively short heating time.
The usual absence of heat shielding, however, reduces the efficiency, requiring more watts
per ampere of emission, and increases the heat that the tube must dissipate. The in-
directly heated type inherently lends itself to more efficient use of the cathode surface,
thereby reducing the heating power required. It has the disadvantage of greater expense
and longer heating time, a factor that is becoming more and more important.
By raising the cathode temperature it is usually possible to raise the emission per unit
area and the emission per watt heating power. However, this raises the rate of coating
evaporation and, if carried too far, shortens the life of the tube.
PEAK ANODE CURRENT. The peak current that a tube is capable of passing with-
out harm depends upon the area, the temperature, and the geometry of the cathode
surface, and somewhat upon the pressure of the gas. If the rated value is exceeded, the
tube voltage drop may increase so that destructive ion bombardment of the catbode
occurs. Also, particles of coating may be mechanically sputtered from the cathode to the
grid, where they are a potential source of grid emission. There is the further possibility
of sudden cessation of current flow, particularly at low gas pressure where the ion density
is insufficient to neutralize the space charge at points where the discharge is the most
dense. This is commonly known as "starvation" and may result in voltage surges in the
circuit in which current has been flowing, sometimes breaking down insulation of the
circuit components. The barium nickelate coating is less subject to this trouble since the
coating is more conductive and will stand a higher arc drop without sputtering or surging.
AVERAGE ANODE CURRENT. Because of the essentially constant tube voltage
drop over the current range, tube heating during operation is a function of average current,
rather than rms current as in most electrical apparatus. Overloading causes excessive
heating of all the tube electrodes and may result in failure because of (1) evolution of
sufficient foreign gas to render the tube inoperative, (2) grid emission and loss of control
due to high grid temperature, (3) arcback due to the high temperature of the anode, (4)
short cathode life due to high evaporation, or (5) mechanical failure of the envelope or
seals.
4-64
ELECTRON TUBES
ANODE CURRENT AVERAGING TIME. When the load is fluctuating, as it might
with a motor load or welding control, the average current must be calculated over a
specified period of time chosen so as to include the worst current conditions. For example,
consider two tubes having a maximum average current of 12.5 amp, a maximum peak
current rating of 75 amp, and an averaging time of 30 sec in a biphase half-wave rectifier
with sufficient inductance to make the d-c ripple negligible. These tubes could supply to
the load 75 amp for 10 sec, 50 amp for 15 sec, or 25 amp for 30 sec out of every 30 sec
without exceeding either peak or average rating.
GRID CURRENTS. In order to prevent overloading of the cathode or the grid through
the grid circuit, a maximum instantaneous grid current and a maximum average grid cur-
rent rating are generally given. Under most conditions of operation, grid currents are
much less than these ratings.
ANODE SURGE CURRENT. The anode surge current is the current which would be
conducted through the anode under fault conditions. The maximum surge current rating
is a measure of the ability of the tube to withstand extremely high transient currents.
The tube should carry the specified current for not longer than a given length of time in
the event of short circuit, but it should not be expected to carry repeated short circuits
without a reduction of life and the possibility of immediate failure. This rating forms a
basis for set design to obtain best tube performance. If sufficient impedance is present to
limit the fault current to this rating, not only will the tube be able to carry that current
in the event of a fault in the circuit, but also the possibility of a fault in the tube itself
seems to be reduced.
TESTS. Tests for maximum average current are generally made by operating the tube
at full load and checking the other ratings which are dependent upon tube temperature,
as described in other sections.
As has been stated, the peak current rating is a function of the emissive capabilities of
the cathode, and the best test of this is, after all, satisfactory life while operating at that
peak current. Several methods have been used for testing the emission, however. A simple
test is to conduct an average current through the tube of a value between the average
and the peak ratings and then measure the tube voltage drop with a d-c meter across the
tube or with the deflecting plates of an oscilloscope connected from anode to cathode.
This method does not discriminate very well between good tubes and bad except for some
small tubes where the average current may be held fairly high for the test. It will suffice
for a rough check on any tube, if used within the rating.
If, with the oscilloscope and a suitable d-c amplifier across the tube, the tube is allowed
to conduct the peak rated current for only a few half-cycles each second, the cathode
temperature is not altered appreci-
ably by the load current, and the
tube drop may be used as an accu-
rate indication of cathode quality.
Figure 5 shows a typical trace ob-
served on a good tube, and Fig. 6
shows a low-emission tube in which
the drop rises to an excessive value
at the maximum current point.
Another method of testing the
emission is to conduct half-cycle
pulses as above, but of increasing
current magnitude, so that the point
is finally reached where the cathode
"sparks" or sputters, giving a broken voltage drop trace. The "sparking point" can be
calibrated against the peak current rating to give a proper test.
In all such tests, the temperature of mercury-vapor tubes should be controlled quite
accurately by an oil bath or controlled-flow air bath.
Surge current tests are generally made by the manufacturer on a given design of tube
to insure a construction sufficiently rugged for ordinary service. Since these tests detract
from the life of the tube, they are not part of the normal test procedure. In general, the
test is made by passing the rated surge current through the tube with some protective
device or control device arranged to open in a definite time, generally 0.1 sec. After the
tube has been subjected to one or more overloads of this type, it is given an operation
test for general performance.
FIG. 5. t Trace on Cathode-
ray Oscilloscope Indicating
Good Emission
FIG. 6. Trace on Cathode-
ray Oscilloscope Indicating
Poor Emission
CONTROL CHARACTERISTICS
4-65
500
17. CONTROL CHARACTERISTICS
Control Characteristic. The control characteristic of a gas tube is a relation, usually
shown by a graph, between critical grid voltage and anode voltage. (IRE Standards on
Electronics, 1938.)
Critical Grid Voltage. Critical grid voltage in a gas tube is the instantaneous value of
grid voltage when the anode current starts to
flow. (IRE Standards on Electronics, 1938.)
Critical Anode Voltage. The critical anode
voltage of a gas tube is the instantaneous
anode voltage when the anode current starts
to flow.
As previously explained, once a thyratron
is passing anode current the grid has little
effect on the anode current, which is then
limited only by the impedance of the load in
the anode circuit. There are, therefore, no
thyratron characteristic curves relating anode
potential, grid potential, and anode current
as there are for vacuum tubes. The relation-
ship between anode voltage and grid voltage
which just permits conduction, known as the
control characteristic, is of considerable im-
portance, however.
In an inert-gas-filled tube, there is a neg-
ligible change of characteristic with normal
temperature changes. There are initial vari-
ations between tubes, however, and there are
further changes in any given tube with life,
the characteristic shifting slightly more nega-
tive as the emission becomes completely
stable, and then shifting more positive as the
end of the tube life approaches. Figure 7
shows the typical control characteristic of a
small thyratron, the range of curves covering
all variations between tubes and with life.
This shows the equipment designer what range he may expect and must design for. In
mercury-vapor tubes, the characteristic changes greatly with mercury temperature and
the temperature must be specified for such a curve, or the range must be extended to
-8 -7 -6 -5 -4 -3 -2 -1
Grid voltage, volts
FIG. 7. Typical Thyratron Control Character-
istic. (Shaded Area Shows Range of Character-
istics.)
3600
3200
2800
g.2400
0
> 2000
< 1600
Q 1200
800
400
•4
L,
Sfc
y
1
&
*b
1°''
V
s^
^s
\
\
\
\
\
s^S
X
\
\
\|
x
^\
X
\\
(c
on
der
se
d H
? '
Te
m
n°
C.)
X
s^
SX
ss
\
\
X
S^x
^\
\
\
\
>
^1
N\
s,
\
\
S
^
s\
^
\
\
^
^
s^S
s,
^
\
^
s^S
\
S
s
N^5
s^s
s
\
\
N^
x
\
^
^
\
X
\
^
^
\
^
v.
\
F
3-1
7
^
\
V
S
S{
^
\
\
\
S
\
X
x
^
^s
N
"v,
X
*«*B
««^
•^
^-
—
:^S
-14 -13 -J.2 -11 —10 -9 -8 -7 -6 —5 -4 -3 -2 -1
Grid Voltage at Start of Discharge
FIG. 8. Control Characteristics for a Mercury-vapor Thyratron
include the variations within the published temperature limits. Figure 8 shows the vari-
ation in the control characteristic of a mercury tube with varying temperature.
4-66
ELECTRON TUBES
aooo
1600
It will be noted that the criticargrid voltages of the tubes shown are negative over the
greater part of the operating range. As long as the grid is more negative than the cathode,
electrons emitted from the cathode cannot flow to the grid, and there is no grid current
from this source. Control is possible therefore with the use of a very small amount of grid
power, which is the advantage of such a "negative grid" tube.
"Positive grid" tubes are available in which it is necessary to force the grid positive
over the entire operating range to fire the tube. To assure non-conduction it is required
only that the grid circuit be opened or the grid held at zero voltage or allowed to float.
These application advantages
are offset, however, by the fact
that considerable power must be
available to drive this type of
tube, and sometimes a discharge
takes place between grid and
cathode before the anode-cathode
path becomes ionized.
SHIELD-GRID CHARAC-
TERISTICS. In four-electrode
tubes the firing point becomes a
function of the potential of both
grids. Figure 9 shows how the
control characteristic curve
varies with shield-grid potentials.
With negative shield-grid poten-
tials, however, the variations
between tubes become excessive
with many types. The shield-
grid signal may be used as a con-
trol to switch the characteristic
in or out of the operating range
of the circuit, and in some cases
may even be used, with the nec-
essary adjustments, to obtain a
desired control curve.
\
\
\.
\
V
\
\k
\
\
\
\
\
\
2-
\
\
\
\
\P
\
\
\
\
\
\
\*
\
\
\
\
\
\
v
V
%>•
\
\
\ \
\
\
\
\
\JT
\
\
A
V
\
\
^
v
p
V
\
\ \
\?
^
\
\
\
\
V/
\
\ \
\
\
\
\
\
\
\ \
\
\
\
A
\
\
\
\
\
v
\,
\
\
\
. \
\
\
\
\\
\
\
\
\
\\
|N\
\
\
\
\
\
^
jA.
^=
=
— — i~»
—14 -12 -JO -8 -6 -4 -2 0 +2 4-4
Control Grid Voltage
FIG. 9. Control Characteristics for Shield-grid Type of Thy-
ratron, Showing Effect of Shield Potential
GRID CURRENTS. The grid currents in a thyratron, both before and after discharge,
are extremely important in deterrnining the necessary grid power or the permissible
impedance in the grid circuit.
Critical grid current in a gas tube is the instantaneous value of grid current when the
anode current starts to flow. If a high grid resistance is used and this critical grid current
—22 -20 -18 -16 -14 -12 —10 —8 -6 -4 -2
FIG. 10. Grid Voltage-Grid Current Curves after Breakdown in Three-electrode Thyratron
becomes excessive, owing to overheating and grid emission, enough voltage drop across
the grid resistance may result so that the available grid supply voltage is not sufficient to
CONTROL CHARACTERISTICS
4-67
800
600
>400
U-
Tub's (
control the tube. This current, then, becomes a limitation on the grid supply voltage and
impedance and on the time constant with which the grid circuit can operate.
Figure 10 shows the grid current in
a 2.5-amp average, three-electrode
thyratron after discharge has occurred.
Negative values indicate positive ion
current to the grid from the discharge,
and positive values indicate electron
current. A four-electrode tube, other-
wise similarly designed, would have
roughly one-tenth the amount of grid
current under these conditions.
Figure 11 shows the grid current for
various anode voltages immediately
before the start of discharge on the
same three-electrode tube, and Fig. 12
shows the same for the equivalent
four-electrode tube.
TESTS. The control characteristic
should be tested to the specified limits,
FIG. 11.
Grid Current before Breakdown in Three-
electrode Thyratron
-2 -1
Grid Ctrrreat in Microamperes
usually at two or more values of anode
voltage. A sufficient d-c control grid
voltage should be applied to prevent
conduction (or firing) , through a low grid resistance. The specified d-c anode voltage is
applied and the control grid gradually made more positive until breakdown occurs to
the anode, at which time the critical grid voltage is observed. Condensed-mercury
temperature should be controlled.
The critical anode voltage may
be observed by holding the grid at
zero voltage and increasing the
anode supply until firing occurs.
The critical grid current is gen-
erally measured as shown in Fig.
13. The tube is first operated at
the full average current rating as
indicated by a d-c ammeter in the
anode circuit, in order to heat all
the parts to their operating tem-
peratures. With the grid resistor
rg short-circuited, the grid supply
voltage is then made more nega-
tive until the tube ceases to con-
duct. This is possible since an a-c
supply is used and the tube does
not conduct during the negative
half-cycle. This voltage reading is
denoted by V\. Another reading
is. ^^dmtely taken with rg in the
circuit. With most tubes, a value
800
s,600
"5
| 400
200
0
O.C
^
\
^
\
\
\
Tu
e
Col
d
^
Ti
be
He
l\
\
1,
F(
>c
35
/
***
^
JOS 0.004 0.003 0.002 0.001 C
Grid Current in Microamperes
FIG. 12. GridT Current before Breakdown in Shield-grid Thy-
ratron Tube
of rg between 10 and 100 megohms
is sufficient to make the second reading, Vz, considerably higher than Vi. Since the actual
critical grid voltage measured directly at the grid is the same in both measurements, the
difference in the two readings must be accounted for as voltage drop in the resistor r&.
The grid current, therefore,
is given as: i ~ (V% — V\}/rg.
This reading of grid current
includes currents from the
ionized space to the grid,
leakage currents, and grid
emission. If the test is made
without previous operation
of the tube, the grid-emission FlG> 13^ cSxwak Used to Check Grid Emission
factor will be eliminated.
DEIONIZATION TIME. Deionization time of a gas tube is the time required for
the grid to gain control after interruption of the anode current. This varies with condensed-
4-68
ELECTRON TUBES
mercury temperature, anode current, anode voltage immediately after discharge, grid volt-
age, grid circuit impedance, and a number of other factors. Not only is the peak anode
current just before discharge ceases
important, but the wave shape is
also, since in some cases the ioniza-
tion due to an earlier peak current
may decay less rapidly than the
current, thus requiring a longer
deionization time. Forcing the
anode and grid negative immedi-
ately after the discharge has ceased
decreases the deionization time
FIG. 14. Circuit Used to Check Deionization Time
D-c
supply
FIG. 15. Typical Anode-cathode Voltage Trace during
Deionization Time
since positive ions are then attracted to these electrodes, where they are neutralized.
To restore control to the grid it is not necessary to remove all the ions from the grid-
anode space but only to reduce the
number to a value sufficiently low so
that the grid sheaths overlap enough to
prevent discharge when a positive anode
potential is again applied. Ions may
still be present near the anode or near
the cathode, with the grid having con-
trol. This shows why the grid voltage
and stiffness of the grid circuit may be
relatively more important in deioniza-
tion than the anode circuit.
Since deionization time varies so
widely with all these variables, it is es-
sential to know all these conditions under which a measurement has been made. A recom-
mended circuit for making such tests is shown in Fig. 14. The operation is briefly as follows :
The tube under test is conduct-
ing a specified d-c current. The
capacitor C is connected in parallel
with the load resistor R and there-
fore charges so that the negative
capacitor plate is connected to the
tube anode. When the switch S
is closed, the capacitor makes the
anode voltage of the tube instantly
negative, thus stopping the dis-
charge. The capacitor then re-
charges through the load resistor
until the anode voltage of the tube
and the capacitor voltage are equal
to the supply voltage. The rate at
which this anode voltage becomes
positive depends upon the value of
the capacitor C and of the load
resistor, r. These values can easily
be used to calculate the length of
time from stopping of the discharge
until the anode voltage again be-
comes positive, approximately the
point at which the tube would
conduct if deionization is not com-
plete. At the capacitor setting at
which the tube fails to control, the
deionization time can be calculated
from tfcp formula T = 0.693rC.
Any desired grid conditions may be
used and the effect of these factors
determined. Figure 15 shows a
typical anode voltage trace during
the test operation.
1000
900
800
700
TD
§ 600
3
e
-H500
c
0,400
E
300
200
roo
D
eio
niz
atic
nl
im
/
/ y
/
/
y
^
^
,-i
^x
^
/
^
x^
/
/
r
o)
/
1
' rt.
/
Y
^
\
A*
•^
£,
r
^
P
iak
Ct
rre
nt
420 A
CJon
• Ang
e
T!
G
rid
Re
iopq
V
It
ge
25
0V
10 20 30 40 50 60 70
Condensed Hg - Temperature°C.
80
FIG.
16. Deionization Time Shown as a Function of
Mercury Temperature
Other modifications of this circuit may be used to allow greater variation of anode
voltages, or inverter circuits may be set up which will operate the tubes under more ex-
PULSE THYRATRONS
4-69
treme conditions. Figures 16, 17, and 18 show the effect of some of the factors mentioned
above.
1200
1100
1000
900
800
Oi
I 700
e
o 6QQ
1
!/
A
/
i
/
!/
/
X
r
s
t
/
*,
%
&//<•
/
i
/
&
1
/
,
//
'&
x
/t
x'
i
^
^
"
'•s.
» 500
400
800
200
100
n
Deionization Time
vs.
Current Density
Grid Bias -150V.
Grid Resis. 500n
Voltage 250V.
Current Density thro Baffle Holes - A-mps./Sq,. Irk
FIG. 17. Deionization Time Shown as a Function of Tube Current Density
1IUU
1000
900
800
700
1
geoo
1
£ 500
is
p
300
200
100
n
~-"
-—
— —
ea
^
***
**^
^*
^
x'
'^
~~~
.. —
-^~
/
:.CJ.
At
/
x
a^*
^^
**"
/
^,
X
*-— •
- —
X
f f
-\
&
^
X]
^,
X
X1
•**
-
x^
x
Deionization Time
vs.
Grid Resistance
Peak Current 420 A
Cond. Angle 10°
Voltage 250V.
Cond. Hg TemD. 30°C
\
100 200 300 400 500 600 700 800 900 LQOO
Grid Resistance in Ohms
FIG. 18. Deionization Time Shown as a Function of Grid Eesistance
18. PULSE THYRATRONS
As described in Section 9, Pulse Techniques, many circuits have been developed in
which the currents are essentially square-wave pulses. One application of this sort pro-
vides modulated power for driving a magnetron; here a thyratron is used to discharge a
4-70 ELECTRON TUBES
pulse-forming line or network, previously charged to a high d-c voltage, through a pulse
transformer into the load. The thyratron is in series with the line and load, and it carries
a pulse current of magnitude determined by the voltage charge on the line and the com-
bined impedances of the line and load.
PULSE VOLTAGES. During the charging of the line, the thyratron is subjected to
the full instantaneous network voltage, so that it must be capable of holding off this
voltage. It is generally desirable that this be done with zero grid bias on the tube, and
consequently pulse tubes are designed so that they will fire only when considerable positive
voltage is applied to the grid. This is generally of the order of 50 to 100 volts, although a
higher voltage may be required by the manufacturer's data in order to insure that firing
will occur with a minimum of time variation.
Time jitter is a common term for expressing the variation in the length of time from
application of the grid firing voltage until start of the anode current pulse. Although the
actual amount of this delay time is not so important, any variation tends to destroy the
usefulness of systems in which the pulse may be as short as 0.1 microsecond. In order to
keep the time jitter appreciably lower than this figure, the trigger pulse applied to the
grid should have a steep wave front and a peak voltage appreciably higher than the mini-
mum required to cause ionization. The internal impedance of the trigger supply must
also be low enough to provide sufficient grid power to assist in accurate firing.
At the end of the anode-current pulse, depending on the ratio of load and line imped-
ances, the voltage across the line, and hence across the tube, may become negative. The
allowable negative voltage is limited because of the possibility of the remaining ionization
causing arcback. After deionization is complete, the inverse voltage may be increased,
generally to about the forward rating; deionization will generally occur in a fairly small
percentage of the total time of application of inverse voltage and will allow the use of a-c
charging voltages, other factors being satisfactory.
Tubes are tested for their voltage capacity by operation in a pulse circuit at the required
forward voltage, peak pulse current, pulse width and repetition rate, and inverse voltage,
and with a grid circuit which represents the minimum driving conditions which may be
allowed.
PULSE CURRENTS. Pulse operation for thyratrons was not originally developed for
industrial applications, and the life expectancies under such operation have been somewhat
lower than those of other uses or other tubes. Cathode processing requirements are dif-
ferent, to the end of obtaining from 10 to 20 times the peak current density that is obtained
from industrial tubes. These currents are limited in duration, however, to a pulse width
of the order of 5 microseconds.
Many tubes designed for industrial operation are found to operate satisfactorily in
low-power pulse circuits at much higher currents than their nominal ratings, and satisfac-
tory pulse ratings have been developed for some industrial tubes.
Pulse tubes are generally rated for a maximum pulse repetition rate, pulse width, aver-
age current, and duty. For service in which none of these factors vary with time, the
pulse width (in seconds) times the repetition rate (in pulses per second) will give the duty,
or fraction of the total time, during which the tube is actually carrying a current pulse,
This also serves as a relation between the peak and average currents, and thus limits the
heating of the tube electrodes. In some applications it may be desirable to operate the
tubes at a varying repetition rate; in this case the duty is sufficient to define the average
current, and it becomes necessary to consider the minimum amount of time allowed be-
tween adjacent pulses to take care of deionization.
Because of the type of gas used in order to meet the strict deionization requirements,
and the current densities used, the tube voltage drop during the pulse is inherently high.
In addition, ionization requires some amount of time, during which time the arc voltage
will be even higher. As a result, the tube voltage drop may rise to an initial value of 100
to 300 volts and then drop during the pulse to a value of 50 to 100 volts, these figures
depending on the type of tube and other factors. A value may be read at some specific
time during the pulse as an indication of tube quality, or the tube voltage may be plotted
against the tube current on an oscilloscope, the shape of the resultant curve serving as a
basis for judgment. In this case the voltage is generally higher during the rising current
than during the falling current, and the area enclosed in the corresponding traces is an
indication of the amount of ageing of the cathode during conduction. Information for
the proper testing of any tube type may be requested of the manufacturer.
i* CONSTRUCTION. Although some industrial types of tubes have found pulse appli-
cations, these have been at low repetition rates and voltages, and most of the usable tubes
have been designed specifically for pulse operation.
The cathodes are indirectly heated, since filamentary types have not been found satisfac-
tory. Heating times are generally in the order of 1 to 3 min. This comparatively short
HOT-CATHODE THYRATRON TUBES 4-71
heating time has been obtained by winding light heater wire either inside the cathode
cylinder or outside a cylinder which is coated on the inside and which may have vanes
projecting toward the inside to increase the emitting area. The alkali-earth oxides are
used for the emissive coating.
The ionizing medium is usually hydrogen because of its light weight and high ion mobil-
ity and consequent speed of deionization. Especial care must be taken in processing,
however, because of the susceptibility of hydrogen to cleaning up into the parts, particu-
larly in the presence of contamination. For some of the tubes, high-purity alloys are used
which are not required in the ordinary tube.
The anode must be completely shielded from any possible glow discharge or arc except
the normal discharge, and it is surrounded at close spacing by the grid. In addition to the
usual openings through the grid, an additional shield is placed directly below these open-
ings and connected to the grid proper. This shield assures that the tube will maintain its
highly positive characteristic and operate satisfactorily at high voltage.
Most of the applications have been met by three tube types, one operating at a pulse
voltage of 3000 volts and a pulse current of 35 amp; the second at 8000 volts, 90 amp;
and the third at 16,000 volts and 325 amp.
19. INSTALLATION AND OPERATION OF HOT-CATHODE THYRA-
TRON TUBES
For any particular application complete data should be obtained from the tube manufac-
turer. Observation of the instructions will be amply repaid in satisfactory operation and
long tube life.
FILAMENT CIRCUIT. The greatest single cause of unsatisfactory tube operation in
the past has been incorrect filament voltage. Too low a filament voltage results in low
emission and sputtering of the cathode which will give very short tube life and may pre-
vent the tube from ever operating satisfactorily. Too high a filament voltage results in
an excessive rate of evaporation of cathode material which results in short tube life. A
filament-voltage variation of ±5 per cent is generally permitted. Line-voltage variations
outside the specified ±5 per cent limits for a very short time, such as 5 or 10 sec, are not
generally very harmful in the cathode-type tubes where the cathode temperature changes
rather slowly. If excessive voltage variations are experienced and no corrective apparatus is
available, it is sometimes possible to put the apparatus into operation by so adjusting the
filament voltage that it does not drop more than 5 per cent below the rated value during
the worst periods of sustained low voltage. Under these conditions the average filament
voltage will probably be high and tube life will be shortened but not to the same extent as
with too low a voltage.
CATHODE HEATING TIME. In some of the smaller quick-heating filamentary
thyratrons it is possible, under some conditions of operation when the anode voltage and
current are rather low, to apply both filament and plate voltages simultaneously without
causing excessive damage. However, when full rated current is to be drawn or when a
slower indirectly heated cathode is used, it is essential to provide some means whereby
the tube will not pass anode current until the cathode is up to operating temperature.
This may be accomplished by a switch in either the anode or load circuit or by proper
bias on the grid. Wherever it can be economically justified, a time-delay relay or circuit
may be used to give this protection. Such a relay will also provide protection in the event
of a power failure.
TUBE HEATING TIME. An inert-gas-filled thyratron is ready to operate as soon as
the cathode comes up to temperature. It should be noted, however, that in a mercury-
vapor tube this is not always true. The condensed-mercury temperature must be within
the rated limits before the tube is operated. Under conditions of low ambient temperature
where it is desired to bring the tubes up to operating temperature quickly, tube enclosures
and external heaters may be advantageous.
INITIAL HEATING. During shipment of mercury-vapor tubes the mercury may have
become spattered over the tube electrodes. When first put into service the tube should be
allowed to heat long enough to evaporate the mercury from the electrodes and to distribute
it properly before anode voltage is applied. This may take a half hour or longer, depend-
ing upon the size of the tube.
ANODE CIRCUIT. Tubes should not be used in circuits where the voltages are higher
than the rated peak inverse or peak forward voltages of the tubes. If there is a possibility
that transients may be present, a cathode-ray oscilloscope or calibrated sphere gap across
the tube may prove very useful in determining to just what voltages the tube is sub-
jected.
4-72 ELECTRON TUBES*
CURRENT OVERLOADS. The low, essentially constant, voltage drop common to
gas-filled tubes makes it possible to overload them injuriously to a greater extent than
most hard-vacuum tubes, which have a rising voltage drop with increasing current. Once
a thyratron tube is conducting, the current is limited only by the impedance of the load
circuit. If it should be connected to a very low-reactance source of power with no load
interposed, an abnormal current might flow, destroying the tube in a fraction of a second.
A number of tubes are ruined in this way by experimenters, particularly those who are
familiar with hard-vacuum tubes but who do not appreciate fully this important difference.
For this reason it is very important to make sure that some current-limiting impedance is in
series with both the anode and grid leads when voltage is applied.
This low, constant voltage drop makes it possible to impose heavy peak current over-
loads on the tubes without drawing excessive average current as indicated by a d-c ammeter
directly in series with the tube. Unless sufficient reactance is present in the circuit, these
peaks may be experienced when tubes are used in rectifier applications with capacitors
connected directly across the output, when tubes are used to charge storage batteries, or
when they are operating into any type of counter emf load. Although calculations may
sometimes be made, it is generally safest to check tube currents with an oscilloscope when
high peak currents are suspected.
REACTANCE OF POWER SOURCE. It is desirable to include enough reactance in
the anode transformers or other sources of power to limit the tube short-circuit currents
under any type of fault or failure to a value not greater than the surge current rating of
the tube and to provide protective fuses or other interrupting devices to open the circuit in
a reasonably short time, generally not in excess of 0.1 sec. Experience has shown that
tubes operate much more satisfactorily in circuits in which this precaution is taken than
in ones in which no such protection is provided. Various theories have been offered in
explanation, but the fact has been well proved that high-reactance circuits give long tube
life and low-reactance circuits give short tube life. In multitube circuits arcback of one
tube often overloads the others, and again the circuit reactance must be depended upon
to prevent permanent injury to these tubes. If excessively low-reactance transformers
are used and if tube failures are encountered which show evidence of heavy overloads, such
as blown-up stems or cracked seals, a small resistance or inductance placed directly in the
anode lead of each tube will often stop the trouble.
GRID CIRCUIT. Usually the source of grid power itself has sufficient impedance to
prevent excessive grid current from damaging the tube. If any doubt is felt on this score
a grid resistor should be used to prevent accidents. However, in certain types of inverter
circuits it is advisable to use a relatively stiff grid circuit to help speed up deionization.
In the selection of a resistor the grid-current specification of the particular tube to be used
should be considered so that difficulty will not be experienced through the loss of bias
caused by the flow of grid current in the grid resistor. This resistor should, however, be
large enough so that the voltage measured directly at the grid with the tube conducting
does not exceed its rated value with the normal operating grid-supply voltage.
20. COLD-CATHODE TUBES
The term "cold-cathode tube" refers to tubes in which, in general, the discharge is the
self-sustaining glow type previously described.
Since 110 cathode heating is required, the cathode life is not affected by standby opera-
tion, and these tubes are particularly adapted to relay circuits of infrequent operation, if
the current requirement is sufficiently small, in addition to the familiar regulator and
rectifier applications.
Cold Cathode. A cold cathode is a cathode operating at a temperature at which
thermionic emission is negligible.
Starter (or control anode). A starter of a cold-cathode tube is an electrode ordinarily
used in conjunction with a cathode to initiate conduction
Control Gap. A control gap of a cold-cathode tube is the conduction path between a
starter and cathode in which conduction is ordinarily initiated.
Main Gap. A main gap of a cold-cathode tube is the conduction path between a
cathode and a principal anode in which the principal conduction ordinarily takes
place.
Anode Breakdown Voltage. The anode breakdown voltage of a cold-cathode tube is
the anode voltage required to cause conduction to take place in the main gap when the
control gap is not conducting.
Starter Breakdown Voltage. The starter breakdown voltage of a cold-cathode tube is
the starter voltage required to cause conduction to take place in the control gap.
COLD-CATHODE TUBES
4-73
Transfer Current. The transfer current of a cold-cathode tube is the control-gap cur-
rent required to cause conduction in the mam gap with positive voltage applied to the
anode.
Regulation. Regulation of a cold-cathode tube is the difference in voltage drop ob-
tained over a range of conducted current.
Inverse Anode Current. The inverse anode (or starter) current is the electron current
flowing from the associated circuit to the anode (or starter) of a cold-cathode tube.
Anode Drop. The anode drop of a cold-cathode tube is the main-gap voltage drop
after conduction is established in this gap.
Starter Drop. The starter drop of a cold-cathode tube is the control-gap voltage drop
after conduction is established in this gap.
VOLTAGE REGULATOR TUBES. Two-electrode, inert-gas-filled cold-cathode tubes
are generally operated within a certain range of d-c load currents within which the tube
voltage drop remains essentially constant. For instance, such a tube might break down
or become ionized with a potential of 125 volts on the anode and then operate within 3 or
4 volts of a 90-volt tube drop within the specified current range. As with the hot-cathode
tubes, the variation in supply voltage therefore appears across the load resistance, and it is
essential that this resistance be sufficient to maintain the load current within the required
value. Some calculations are generally necessary to insure that adequate starting voltage
is also available when the supply voltage to be regulated falls to its minimum, value.
Since regulator tubes are designed to conduct current in one direction only, they gen-
erally have one small electrode and one large electrode, the large one acting as the cathode.
Tube life depends upon the current density on the cathode (and therefore the size of the
cathode), since sputtering of the metal will occur if the element is overloaded.
THREE-ELECTRODE COLD-CATHODE TUBES. A third electrode or starter may
be introduced into a cold-cathode tube to control the starting of the discharge. As with
hot-cathode tubes the starter has no appreciable control once the discharge has occurred
in the main gap until the anode potential has
dropped below the tube voltage drop (some-
times called sustaining voltage).
The use of these tubes as relays is obvious
because of their control characteristics. An-
other property of such a tube is that, although
some inverse anode current will be conducted
with negative anode voltage, the breakdown
voltage in this direction is somewhat high
and the anode drop increases rapidly as
current increases. Figure 19 shows this
characteristic. With the starter connected
to the anode through a high resistance, the
forward breakdown voltage will be much
below the normal main-gap breakdown value
and the tube will operate satisfactorily as a
rectifier. The circuit must be such, of course,
that peak inverse anode current or voltage
ratings are not exceeded.
The starter drop is quite independent of
control-gap current, and the tubes are used
as voltage regulators with the cathode and
starter as electrodes.
80
40
-
eo
-160
-200
-30 -20 -10 0 10 20 30 40
Anode current, mlUiamperes
FIG. 19.
Typical Cold-cathode-tube Character-
istic
The mechanism of operation of the starter is similar to that of the grid in a positive-grid
thyratron. When positive voltage is applied to the starter, a small electron current known
as a Townsend current will flow from the cathode. As the voltage and the Townsend cur-
rent are increased, a point is reached at which ionization occurs in the control gap. The
control-gap current may then be increased by the control circuit until the transfer current
is reached, at which point (depending upon the anode voltage) conduction occurs to the
anode. At the anode breakdown voltage, conduction will occur without ionization in the
control gap, and therefore the transfer current is zero. At the other extreme, the tube will
not sustain a discharge at less than the anode drop, and hence the transfer current required
at this point is infinite. Figure 20 shows a typical transfer-current characteristic. It is
apparent that the anode operating voltage, when starter control is expected, must lie
somewhere between the anode drop and the anode breakdown voltage.
The control characteristics are subject to variation during life but may be expected to
remain constant within 5 or 6 volts during most of life. Variation during shelf life may
*be of the same order of magnitude depending upon the length of storage and the light
4-74
ELECTRON TUBES
conditions for those tubes which do not have an opaque coating. The effect of light is
negligible for medium light levels but will be appreciable at levels approaching darkness
or direct sunlight, the numerical value of breakdown voltages decreasing as light intensity
is increased, and conversely with decreased intensity. Most variations occurring during
storage will disappear after a few seconds of operation.
170
160
150
140
S
£130
JS120
g
I 110
100
90
80
70
8 10 12 14 16 18
Transier current, microamperes
20 22 24
FIG. 20. Typical Transfer Current Characteristic
TEST FOR COLD-CATHODE TUBES. Because of the effect of light and storage
upon control characteristics, it is generally advisable that all tests be made with moderate
illumination and with a few seconds of current conduction immediately before the test in
order to stabilize the readings. Because of the low values of transfer current some errors
may be introduced if capacitance effects are ignored, and it is therefore important that
the starter resistance be placed immediately adjacent to the starter electrode.
Breakdown voltage is measured by applying a positive d-c voltage to the anode and
increasing it until the tube conducts current. The minimum value of voltage required to-
start conduction is measured. After the tube conducts, the tube drop may be measured at
specified current values and the regulation thereby determined. For three-electrode tubes
the anode breakdown voltage is measured as above, except with the starter connected to-
the anode through a resistance generally not exceeding 50,000 ohms.
Transfer current is measured by applying the specified d-c anode potential and a positive
starter voltage, with sufficient starter resistance to limit the starter current to less than
the transfer value. The starter current is then increased until conduction takes place in
the main gap, at which point the transfer current is measured by means of a microammeter
in series with the starter. Care must be exercised to insure that the starter is electrically-
connected at every instant during this test.
STROBOTRON TUBES. A modification of the three-electrode cold-cathode tube
described is commercially called the Strobotron. This tube commonly has two control
electrodes or grids together with the cathode and anode. The cathode is coated with a,
cesium compound, which breaks down during conduction and liberates free cesium. The-
tube is inert-gas-filled, and conduction occurs by formation of a cathode spot on the metallic
cathode surface by concentration of a glow discharge. The voltage drop is therefore much
lower than that of a glow discharge. These tubes are commonly used with neon gas as
a source of high-intensity light for stroboscopic purposes but may also be used for control
or relay purposes. Capacity is limited by cathode heating during conduction and by ion
bombardment of the cathode as with other cold-cathode tubes. For this reason, although
very high peak currents can be handled, the average current rating is generally
quite low, £$£
A capacitance is generally used across the tube in operation. This capacitance is dis-
charged through the tube in order to provide very high instantaneous current. It also
serves as a means of stopping the discharge, since, as the capacitance discharges to the
tube drop, the conduction changes to a glow rather than an arc. This immediately raises
the tube drop and the conduction ceases, the tube becoming deionized before the capacitor
recharges to sufficient voltage to maintain even a glow discharge. Operation at too high.
POOL-CATHODE TUBES
4-75
a frequency, or -with improper circuit conditions, will frequently maintain a glow discharge
in the tube and lose the advantage of the tube's capacity for high peak currents.
With this tube as with other cold-cathode tubes life is a function of average current and
conduction time, there being no appreciable deterioration during storage.
Available types of tubes are shown in Table 2.
Table 2. Available Types of Cold-cathode Tubes
Type
Desig-
nation
Cathode Current,
milliamperes
Anode
Voltage
Drop
Breakdown
Voltage
s — starter
a = anode
Remarks
Average
Peak
874
RCA
10-50
90
125a
Voltage regulator
991
RCA
2
3
4&-67
87a
Voltage regulator
BR
Ray
50
60
Rectifier
OA2
S, Hy,
5-30
150
I55a
Miniature voltage regulator
RCA
OB 2
Hy
5-30
105
133a
Miniature voltage regulator
OA3/VR75
GL-, S,
5-40
75
lOOa
Voltage regulator
RCA
OB3/VR90
GL-, S
10-30
90
HOa
Voltage regulator
OC3/VR105
GL-, S, Hy,
5-40
105
11 5o
Voltage regulator
RCA
OD3/VR150
GL-, S,
5-40
150
I60a
Voltage regulator
RCA,Hy
1B46
S
1- 2
79-85
225a
Miniature voltage regulator
1B47
S
1- 2
75-90
225a
Miniature voltage regulator
1B64
S
1- 2
65-75
225a
Miniature voltage regulator
31 3C
WE
35
100
75 at 20 ma
70s
Control tube
313CC
WE
18
50
75 at 20 ma
72s
Control tube
359A
WE
15
40
75 at 10 ma
75s
Control tube
395A
WE
13
35
75 at 10 ma
77s
Control tube
OA4G
S, RCA
25
100
70
75-90s
Control tube
1C21
RCA
25
100
73
66-80s
Control tube
618
KU-
15
100
180
Control tube
1B48
Ray
6
50
1 00 at 6 ma
800a
High-voltage rectifier
Prefix Used by
GL- General Electric Company
Westinghouse Electric Corporation
KU-
Letter
WE
RCA
Ray
S
Hy
Indicates
Western Electric Company
Radio Corporation of America
Raytheon
Sylvania Electric Products, Inc.
Hytron Radio and Electronics Corporation
21. POOL-CATHODE TUBES
Pool Cathode. A pool cathode is a cathode in which the principal source of electron
emission is a cathode spot on a metallic pool electrode.
Cathode Spot. A cathode spot is an area on the cathode of an arc from which electron
emission takes place at a current density of thousands of amperes per square centimeter
and where the temperature of the electrode is too low to account for such currents by
thermionic emission.
Pool Tube. A pool tube is a gas tube with a pool cathode.
Single-anode Tube. A single-anode tube is an electron tube having a single main anode.
Multianode Tube. A multianode tube is an electron tube having two or more main
anodes and a single cathode.
Ignitron. An ignitron is a single-anode pool tube in which an ignitor is employed to
initiate the cathode spot for each conducting period.
Excitron. An excitron is a single-anode pool tube provided with means for maintaining
a continuous cathode spot.
Pumped Rectifier. A pumped rectifier is a rectifier which is continuously connected
to evacuating equipment during operation.
Sealed Tube. A sealed tube is a tube which is hermetically sealed after degassing.
Ignitor. An ignitor is a stationary electrode which is partially immersed in the cathode
pool and has the function of initiating a cathode spot.
4-76
ELECTRON TUBES
As mentioned previously, tubes of the pool-cathode type make use of the self-sustaining
form of discharge. The cathode dark space is very small because of the high current den-
sity, and the resulting high voltage gradient is assumed to cause field emission and thus
maintain the high current density at an arc voltage drop near that of the ionization voltage.
Since there is no emissive material to be damaged, the pool cathode is capable of carrying
extremely high currents without any deterioration. Tubes havdng such cathodes can
therefore be used in applications where very high peak currents are required for short
periods of time, or where it is desirable that a high short-circuit or arcback current be
allowed without damage to the tube. This current can be much higher proportionally
than for a hot-cathode tube. The pool cathode also has the advantage of not requiring
heating time.
On the other hand, the pool tube requires auxiliary circuits for maintaining ionization
or for starting the ionization during each operating cycle. The size of the tube and the
corresponding volume of ionization increases the difficulty of building high-voltage tubes,
or those with rapid deionization. Further, because of the amount of current capacity,
water cooling is required for most types, and corresponding protection must be provided
to insure proper water flow and water temperature at all times.
Available types of pool tubes are listed in Table 3.
Table 3. Available Pool-cathode Tubes
Type
Designation
Typical Ratings
415
681/686
652/657
271
235-A
651/656
655/658
258-A
259-B
679
653-B
238-B
ES-8-01
507
688
427
506
8-in. tank
10-in. tank
1 0-in. tank
1 2-in. tank
6-EP-20-01
1 6-in. tank
16-in. tank
15-in. tank
20-in. tank
2 2-in. tank
6-EP-20-11
HF-26
GL-
WL-
WL-
GL-
GL-
WL-
WL-
GL-
GL-
WL-
WL-
GL-
Allis-Chalmers
GL-
WL-
GL-
GL-
Westinghouse
General Electric
General Electric
Westinghouse
Allis-Chalmers
General Electric
General Electric
Westinghouse
General Electric
Westinghouse
Allis-Chalmers
Allis-Chalmers
300-kva, 22.4-amp average, welder control ignitron (sealed)
300-kva, 22.4-amp average, welder control ignitron (sealed)
600-kva, 56-amp average, welder control ignitron (sealed)
600-kva, 56-amp average, welder control ignitron (sealed)
1200-kva, 140-amp average, welder control ignitron (sealed)
1 200-kva, 140-amp average, welder control ignitron (sealed)
2400-kva, 355-amp average, welder control ignitron (sealed)
2400-kva, 355-amp average, welder control ignitron (sealed)
600 volts d-c, 200 kw (output of 6 tubes),* rectifier ignitron (sealed)
250 volts d-c, 150kw
600 volts d-c, 200 kw (output of 6 tubes),* rectifier ignitron (sealed)
250 volts d-c, 150kw
600 volts d-c, 500 kw (output of 6 tubes),* rectifier ignitron (sealed)
250 volts d-c 300 kw
600 volts d-c, 500 kw (output of 6 tubes),* rectifier ignitron (sealed)
250 volts d-c, 300 kw
600 volts d-c, 500 kw (output of 6 tubes),* rectifier excitron (sealed)
250 volts d-c, 300 kw
600 volts d-c, 1000 kw (output of 6 tubes),* rectifier ignitron (sealed)
250 volts d-c, 600 kw
600 volts d-c, 1000 kw (output of 6 tubes),* rectifier ignitron (sealed)
250 volts d-c, 600 ]|cw
350-volt peak 1 0-amp glass demonstration ignitron (sealed)
9000-volts d-c, 8100 kw (output of 6 tubes),* rectifier and inverter
ignitron (sealed)
600-volts d-c, 1000 kw (output of 6 tanks),* rectifier ignitron (pumped)
600-volts d-c, 1000 kw (output of 6 tanks),* rectifier ignitron (pumped)
250-volts d-c, 625 kw
3000 volts d-c, 1 500 kw (output of 6 tanks),* rectifier ignitron (pumped)
600 volts d-c, 1500 kw (output of 6 tanks),* rectifier ignitron (pumped)
250 volts d-c, 750 kw
600 volts d-c, 1500 kw (output of 6 tanks),* rectifier excitron (pumped)
250 volts d-c, 750 kw
600 volts d-c, 2000 kw (output of 6 tanks),* rectifier ignitron (pumped)
250 volts d-c, lOOOkw
3000 volts d-c, 4000 kw (output of 6 tanks),* rectifier ignitron (pumped)
600 volts d-c, 2000 kw (output of 6 tanks),* rectifier ignitron (pumped)
250 volts d-c, lOOOkw
600 volts d-c, 3000 kw (output of 6 tanks),* rectifier ignitron (pumped)
250 volts d-c, 1 500 kw
600 volts d-c, 3000 kw (output of 6 tanks),* rectifier ignitron (pumped)
250 volts d-c, 1 500 kw
1750 volts d-c, 2500 kw (output of 6 tanks),* rectifier and inverter
excitron (pumped)
1000 cycles, 300 kw, multianode frequency changer (pumped)
* These are typical operating conditions rather than absolute maximum ratings.
WL-, prefix used by Westinghouse Electric Corporation; GL-, prefix used by General Electric Com-
pany.
POOL-CATHODE TUBES
4-77
CLASSIFICATION. Pool-cathode tubes may be classified as sealed or pumped units.
In general, the single-anode sealed units are of comparatively lower current capacity, now
being built in the range from about 50 amp average to about 400 amp average. After the
initial exhaust treatment these tubes are permanently sealed and no further pumping is
required. Pumped units have been built largely of metal in either single-anode units or
in a multianode form commonly called a tank. These units have a pump or system of
pumps operating to maintain vacuum. Current capacity of these tanks is in the order of
1000 amp average. Pool tubes may be classified still further as tubes in which there is
continuous ionization and those in which the arc is initiated each time conduction starts
and is extinguished at the end of each conducting period.
MERCURY-ARC RECTIFIERS. The mercury-arc rectifier is a familiar example of
a pool tube in which continuous ionization is maintained.
FIG. 21. Typical Pumped Mercury-arc Rectifier Tank. (Courtesy of G. E. Co.)
These types are made in both glass and metal. The glass types are sealed units with
the mercury pool in the bottom and with glass arms extending out from the main body of
the tube, slightly above the pool level. An anode is sealed into the end of each arm, which
may or may not be bent, depending on the inverse voltage rating of the tube. Some two-
anode types are made for lighting and railway service, but the more extensive applica-
4-78
ELECTRON TUBES
Ferntco Metal Alloy
and Pyrex Type
Glass Seal
tions are in three- or six-anode designs. These applications are mainly outside the United
States and are in railway service and other power usage. A typical six-anode tube wou]ld
have a capacity of the order of 400 amp average at 600 volts.
The arc spot of such tubes is generally formed by tilting the tube so that the mercury
pool forms a circuit with a starting electrode. When this circuit is broken an arc is ini-
tiated and is maintained by one or more auxiliary anodes. These anodes form with the
pool a low-voltage rectifier the purpose of which is to keep enough current (6 or 7 amp)
flowing through the tube to maintain the cathode spot. As the tube current increases,
the cathode spot breaks up into several spots each carrying about the same amount of
current.
These tubes may be given grid-control characteristics by the addition of a grid around
the anode in each arm.
Figure 21 shows an example of a metal multianode pumped rectifier tank rated for
1000 kw at 600 volts. Such tanks operate like the glass tubes except that the arc is ini-
tiated by a probe electrode in the center of the pool. This electrode is magnetically con-
trolled and makes and breaks contact with the pool in order to form the arc spot. loniza-
tion is then maintained by auxiliary anodes such as the one shown on the right-hand side
of the tank, extending from the top cover into the main volume. One of the main anodes
is shown at the left, with a
suitable grid structure sur-
rounding and with addi-
tional baffling below. The
bottom surface of the tank
slopes to allow the return of
condensed mercury to the
pool in the center, and a
water-cooling system ex-
tends completely around the
outside of the tank, under
the mercury pool, and
through a cooling coil and
cylinder in the center of the
tank. This provides a maxi-
mum of cooling area in con-
tact with the arc and thus
provides the best control
of operation. Direction of
water flow is indicated by
arrows in the cooling sys-
tem. The exhaust connec-
tion, vacuum controls, and
pumps are shown at the top
and right of the tank.
Such tanks are built with
voltage ratings as high as
3000 volts direct current
and with currents of the
order of 1000 amp.
IGNITRONS. Figure 22
shows a typical sealed igni-
tron tube. The two enclos-
ing cylinders provide a path
for cooling water, and, since
the temperature of the inner
tube wall is important in
Flow-dlreciiO]
Vanes
Delonization Baffle
Splash-hood Baffli
Tube Support and
'Cathode Connection
Main Graphite Anode
Starting Igniters
•Mercury PooJ.
Cathode
'Seal-off7*
PIG. 22. Sealed Ignitron for Power Rectifier Service,
of G. E. Co.)
(Courtesy
deternuning mercury-vapor pressure and operating capacity of the tube, it is essential
that the required water flow be provided during operation. The graphite anode is
designed for a maximum transfer of heat from its face and for a minimum of heat genera-
tion from the high current flow. Mercury is thrown up from the pool by the action of
the cathode spots, and a splash-hood baffle is placed directly above the center of the
cathode to prevent splashes of mercury from hitting the anode or upper tube walls and
thereby increasing the possibility of arcback. The purpose of a deionization baffle is
easily seen, since it reduces the distance from the ionized ai;ea to a metal part. This part
is particularly important in tubes designed for rectifier service, where the deionization
requirements are more severe than in welder use. The auxiliary anode, also, is used for
POOL-CATHODE TUBES
4-79
rectifier service, where it is desirable to maintain ionization over the conducting period in
order to provide for main anode currents below the value at which the arc becomes un-
1 MYCALEX ANODE INSULATOR
2 MYCALEX INSULATOR (LEAD TO INSULATED BAFFLE)
3 ANODE HEATER COVER
4 ANODE HEATER
5 VACUUM CHAMBER • COVER
€ TWO (2) ALUMINUM GASKETS
7 VACUUM CHAMBER
8 WATER JACKET
9 GRID
10 SUPPORT RING FOR PT. 9
I I INSULATOR FOR PT 9 ( MYCALEX)
I 2 GRAPHITE ANODE
I 3 ANODE STUD
I 4 MERCURY SPLASH BAFFLE
I 5 IGNITOR TIP
I 6 INDIVIDUAL VACUUM VALVE
17 HEAT SHIELD
18 ANODE SPACER
I 9 MYCALEX INSULATOR FOR IGNITOR 8 REUEVMG ANODE LEADS
20 ADJUSTING SCREWS FOR PT. 15
2 1 FLEXIBLE DIA {AND ADJUSTING SCREWS PT 2(
PERMIT ADJUSTMENT Of 1GNITOR IMMEF "
POOL) TO CORRECT VALUE FROM OUTSI
22 RELIEVING ANODE FOR JGNITOR TIP
23 MERCURY SEPARATORS
24 MERCURY POOL (CATHODE)
25 CATHODE CONNECTION
ZS EXHAUST BAFFLE
If EXHAUST PIPE
28 GASKETS (INNER - FORM VAR)
,C OUTER -ALUMINUM)
FIG. 23. Pumped Ignitron Tank. (Courtesy of G. E. Co.)
stable, usually 3 to 4 amp. Tubes for welder applications may be built without the two
baffles and the auxiliary anode. On the other hand, tubes built for high-voltage rectifier
use may have several baffles or grids surrounding the anode in order to provide high- voltage
4-80 ELECTRON TUBES
control and to reduce deionization time, and they may also have two or more ignitors in
order to assure operation in the event of an ignitor failure.
Figure 23 shows a typical pumped ignitron tank, with vacuum-tight joints and flexible
ignitor support to allow adjustment of the ignitor position; the other parts are similar in
use to those in the sealed tube. The sealed and pumped units are used in similar applica-
tions.
IGNITOR CHARACTERISTICS. The ignitor as shown in Fig. 22 is shaped somewhat
in the form of a pencil and is composed largely of boron carbide. The composition is such
that the high temperature of the arc has practically no effect upon the ignitor surface,
and there is no tendency for the mercury to wet the surface unless foreign material becomes
deposited at the contact area.
The ignitor acts simply as a resistor; a current flows through it into the cathode pool
when voltage is applied between the ignitor terminal and the cathode. When sufficient
current flows, an arc is started between ignitor and pool, and conduction is established
through the tube provided that positive anode voltage is applied. Resistance of the ignitor
may vary from 10 to 100 ohms, and ignition may occur at instantaneous currents of 1 or 2
amp with 100 to 200 volts or at 15 to 30 amp with but a few volts applied. The manufac-
turer's data should be consulted to determine the exact ignitor requirements to insure
proper operation throughout the life of the tube.
Formation of the arc may be caused by one or both of two mechanisms. At the point
where the ignitor is immersed the mercury forms a meniscus, so that its surface is separated
from the ignitor surface by very small distances at some points. High-voltage gradients
exist across this space and cause a discharge to start. Another possible method of ignitor
operation is that of developing heat at the several contact points of the rough ignitor
surface with the mercury surface. The rapid heating at these sharp contacts due to the
ignitor current flow causes the mercury to vaporize rapidly and break contact, thereby
starting the desired arc.
Conduction to the anode occurs in the order of 20 to 200 microseconds after application
of the critical ignitor voltage or current.
Ignitor ratings include the maximum allowable peak voltage and peak current ratings,
which insure that the ignitor will not be eroded or otherwise affected during operation. A
maximum average current rating limits the heating which may contribute to short life.
The maximum required peak voltage and current specify the worst conditions of current
or voltage expected for consistent firing, and a circuit designed to provide at least these
requirements will provide satisfactory operation during the tube life.
Since the arcback characteristic of ignitrons depends upon current, voltage and tem-
perature, the tubes are rated for more than one load current depending upon the operating
voltage and duty cycle. For tubes in rectifier service these ratings take the form of two or
more discrete current ratings at corresponding voltages or length of time of operation.
For welding tubes, a curve of demand kva (rms current times rms circuit voltage) vs.
average tube current is used, thus taking into account the on and off times of the welder
as well as the maximum current carried.
IGNITRON TESTS. Because of the size of the tubes and equipment involved ignitrons
are tested where possible in an operation circuit which closely approximates the applica-
tion conditions. Tests at the maximum current, voltage, and duty cycle should give an
indication, within a very short time, of the quality of the tube. The arcback rate is fre-
quently used as a determining factor of this quality. The water-cooling coils are tested
for their capacity to withstand expected water pressures, but more important than this
test may be the user's test of the purity of the water being used, since sediment or scale will
seriously reduce heat transfer from the inner wall of the tube.
Ignitors are generally tested in a simple manner by measuring the resistance from ignitor
terminal to cathode pool under conditions of normal mercury level. A much more severe
test is to apply a specified' firing voltage and measure the time required for the tube to
conduct current, or to measure both the ignitor current and ignitor voltage at which con-
duction takes place.
EXCITRONS. The excitron is a currently available type of metal rectifier, built in
both sealed and pumped units. This type has the advantages of other single-anode
rectifiers for production and maintenance and has the firing characteristics of the multi-
anode tanks in which ionization is maintained continuously.
In general construction, commercially available excitrons are similar to the sealed or
pumped ignitron except that the cathode is insulated from the tube wall, as it is in the
metal mercury-arc rectifiers. This prevents travel of the arc to the wall where the metal
may be vaporized and deposited over other parts of the tube. In the ignitron type of
tube the arc is extinguished every cycle, and this problem is not of major importance.
The arc is established in the excitron by a jet of mercury propelled up from the cathode
GENERAL PHYSICAL REQUIREMENTS 4-81
to contact an excitation anode, causing a temporary short circuit and arc formation. A
magnetically controlled plunger operates the mercury jet when required, and the arc is
maintained, once established, by the excitation anode circuit.
In the use of a control grid around the anode and suitable baffling the excitron is similar
to ignitrons and other rectifiers.
BIBLIOGRAPHY
Hull, Dr. A. W., Gas-filled Thermionic Tubes, /. AJ.E.E., VoL 47, 79S-803 (1928).
Hull, Dr. A. W., Hot-cathode Thyratrons, Gen. Elec. Reo., Vol. 32, 213-223, 390-399 (April and July
1929).
Knowles, D. D., The Grid-glow Tube Relay, Electric J,, Vol. 25, 176-178 (April 1928).
Knowles, D. D., The Theory of the Grid-glow Tube, Electric J., Vol. 27, 116-120 (February 1930).
Livingston, O. W., and H. T. Maser, Shield Grid Thyratrons, Electronics, Vol. 7, 114-116 (April 1934).
Morack, M. M., and H. C. Steiner, Sealed-tube Ignitron Rectifiers, AJ.E.E. Trans., Vol. 61, 594-598
(1942).
Steiner, H. C., A. C. Gable, and H. T. Maser, Engineering Features of Gas-filled Tubes, Elect. Eng.,
Vol. 51, 312-317 (May 1932).
Pike, 0. W., Power Control through Grid-controlled Heavy Current Tubes, Electronics, Vol. 1, 85-87
(May 1930).
Slepian, J., and L. R. Ludwig, A New Method of Starting an Arc, Elect. Eng., Vol. 52, 605-608
(September 1933).
Packard, D., and J. H. Hutchings, Sealed-off Ignitrons for Welding Control, AJ.E.E. Trans.. Vol. 56,
37-40, 66 (January 1937).
Germeshausen, K. J., and H. E. Edgerton, A Cold-cathode Arc-discharge Tube, Elect. Eng*, July 1936,
pp. 790 ff.
Ingram, S. B., Cold-cathode Gas-filled Tubes as Circuit Elements, AJ.E.E. Trans., Vol. 58, 342 ff
(1939).
Arnott, E. G. F-, Ignitor Characteristics, /. Applied Phys., Vol. 12, 660-669 (September 1941).
Winograd, H., Development of Excitron-type Rectifier, AJ.E.E. Tech. Paper, 44-78 (March 1944).
X-RAY TUBES
By S. Reid Warren, Jr.
22. GENERAL PHYSICAL REQUIREMENTS
X-ray tubes may be divided into three general classes: (1) cold-cathode, gas-filled tubes;
(2) hot-cathode, high-vacuum tubes; (3) cold-cathode, high-vacuum tubes. The last-
named tube has been used to produce x-ray exposures of short duration (approximately
1 psec) by field emission (see reference 8). Hot-cathode x-ray tubes are now used almost
exclusively. Nevertheless a description of gas-filled x-ray tubes is of more than historical
interest, since the phenomena of electric discharge in these tubes show clearly the limita-
tions and the necessity for the careful design of all x-ray tubes.
The x-ray tubes employed by Roentgen and his successors in the field of x-ray research
up to 1912 contained an anode, a cold cathode, and sometimes an electrode called the
" anticathode." Only two electrodes are
necessary, although it was alleged that
the presence of the third electrode was
accompanied by greater stability of the
electric discharge through the tube.
They are arranged in a glass bulb in the
manner shown in Fig. 1. The tube is
exhausted to a pressure of a few microns
of mercury. The gas contains a number _ ^
~P f™~ i~ 4. ~«o T* +u«,« ,v „ ^^^«+^«i FIG. 1. Basic Elements of an X-ray Tube in Which
of free electrons. If there is a potential Electrons are Ejected from a Cold Cathode C by Ionic
difference of the order Of 40 to 80 kv Bombardment. G, the glass envelope. A, the anode
across the electrodes of the x-ray tube, disk of platinum, tungsten, or molybdenum. <7, the
thpsp fw AWtrons arA ar^lpratpd in cath°de, made in the form of a segment of a sphere to
tnese tree electrons are accelerated in focus the electrode stream upon a small area of the
the direction of the positive terminal or anode surface or focal spot,
anode. They acquire sufficient velocity
to remove one or more electrons from atoms of gas in their path. Tbe ions formed by the
ejection of these electrons from gas atoms have net positive charges. Under the action of
the electric field these positive ions are accelerated toward the cathode. When the posi-
tive ions impinge upon the cathode, electrons are ejected from it. They in turn are at-
tracted toward the anode and acquire a velocity depending upon the anode-cathode volt-
age. The electrons which impinge upon the anode at high velocity cause the generation
of x-rays near the surface of the anode. As a result of the positive-ion stream passing
toward the cathode and the electron stream passing to the anode, a current flows through
4-82 ELECTRON TUBES
the x-ray tube, which, in accordance with convention concerning the direction of current
flow, is said to pass from anode to cathode.
The process involved in the generation of x-rays at voltages of the order of 100 kv is
extremely inefficient. Of the total electrical energy supplied to an x-ray tube only about
0.01 per cent is transformed into useful x-rays. Of the remainder, the greatest part is
dissipated as heat from the x-ray tube anode.
The current through an x-ray tube of this type cannot be controlled independently of
the voltage. As the parts become heated during operation the gas pressure within the
tube changes, often in an unpredictable manner, apparently influenced as much by the
previous history of the tube as by the contemporary electrical input conditions. If the
pressure within the tube decreases, a higher anode-cathode voltage is required to cause the
flow of a given current. The x-rays generated at high voltage with low gas pressures are
more penetrating than those generated at lower voltages with higher gas pressures. Low-
pressure, cold-cathode tubes and the highly penetrating x-rays generated by operating
them at high voltages are called hard tubes and hard x-rays. Tubes with relatively high
pressure operated at low voltages are called soft, and the radiation so generated is called
soft radiation. The terms hard and soft are purely qualitative.
In spite of ingenious attempts to make a practically useful cold-cathode x-ray tube, it
has been used very little since the invention in 1913 of the hot-cathode x-ray tube by
W. D. Coolidge and his co-workers.
Two important investigations during the period 1908-1913 contributed to the develop-
ment of an x-ray tube in which the current can be varied independently of the voltage.
Langmuir had investigated thoroughly the electronic emission from hot metallic filaments
noted by Edison and earlier by Elster and Geitel. Briefly, to summarize this work, the
following important findings are noted:
1 . Unless the pressure of the gas within the tube is less than about 1 micron of mercury,
positive ions produced in the same manner as those in the gas x-ray tube described above
cause an important variation in the electron output of the filaments. At pressures lower
than this the electrons emitted by the hot body are due apparently entirely to thermionic
emission, and therefore their number depends only upon the cathode material and its
temperature.
2. In general the introduction of various gases causes a considerable decrease in electron
emission, particularly at low filament temperatures. This effect should not be confused
with the effects due to ions formed in the added gas.
3. At very low gas pressures the thermionic current from a tungsten filament varies with
the temperature in the following manner:
T is the absolute temperature; i, the current in amperes per square meter of cathode
surface; for tungsten a = 6.02 X 105 amp per sq m per (degree) 2; b = 52,400 deg K. An
expression similar to this was first developed by Richardson.
4. The operation of a tube with high vacuum is greatly influenced by a space charge
consisting of a cloud of electrons surrounding the hot filament.
Investigators have found that x-rays are generated more efficiently by elements with
high atomic number. Therefore they attempted to find a metal with the following charac-
teristics:
1. High atomic number, to provide efficient x-ray generation.
2. High heat conductivity, to allow for dissipation of the heat generated at the x-ray
tube anode.
3. Low vapor pressure, to assure stable operation.
4. High melting point, to provide sufficient capacity.
5. Ease of machining and relatively low cost.
X-ray tubes employed by workers who immediately followed Roentgen contained
anodes of platinum. It was found subsequently that tungsten was better suited than
platinum in all respects except that it was impossible, by means developed up to that time,
to purify and to machine. A period of several years was required to devise methods for
producing and working tungsten. The manufacture of uniform, standard x-ray tubes
depends upon the carefully controlled processing of the component metal and glass parts.
The method now generally used requires the removal and purification of an oxide of tung-
sten from the ore wolframite. The powdered oxide is formed into blocks and heated in
the presence of hydrogen. After such treatment, the oxide is reduced to metallic tungsten;
the bar contracts but remains extremely weak mechanically. It is, however, sufficiently
strong so that bars about 2 cm square and 15 to 20 cm long may be supported at one end
by a water-cooled copper electrode, while the other end rests in a pool of mercury which is
also cooled. This system is surrounded by a jar through which hydrogen passes. An elec-
TUBES FOE X-RAY THERAPY
4-83
trie current is passed through the tungsten bar, heating it to about 2800 deg cent. Gradu-
ally the metal contracts and becomes mechanically stronger. It is then heated to red heat
in air and swaged. This process consists of operating upon the tungsten bar with tools
which pound it radially from several directions. By this treatment the tungsten becomes
hard, homogeneous, and ductile. It is possible to continue the swaging process until the
bar has been reduced to a diameter of a few millimeters. It may then be drawn into tung-
sten wire by means of diamond dies. The larger bars may be cut or polished by means of
Carborundum. Solid tungsten anodes for x-ray tubes may be constructed from such bars.
Smaller sections can be cut by means of
thin (0.01 in.) rubber disks a few inches
in diameter containing 240-grit Carbo-
rundum and operating, wet, at high
speeds (9000 rpm).
W. D. Coolidge devised an x-ray tube
like the one shown in Fig. 2. He found
that it had the following characteristics:
1. The tube allows current to pass
only in the direction from anode to
cathode.
2. The current through the x-ray
tube is practically independent of the
voltage applied to the anode and cathode
for voltages of 30 to 200 kvp. The current may be varied by changing the temperature
of the tungsten cathode.
3. The area upon the anode over which electrons impinge may be controlled by the
catfcode shield S and by the position of the cathode coil C within this shield.
X-ray tubes are employed for the following purposes:
VOLTAGE CTTKBENT
PUBPOSE LIMITS LIMITS
1. Generation of x-rays for the treatment of disease
(x-ray therapy) 12-2000 kvp 0.1- 30 ma
2. The production of x-ray shadow pictures for medical
diagnosis (roentgenography) 30- 110 kvp 10 —500 ma
3. Industrial roentgenography 30-2000 kvp 0. 1-100 ma
4. X-ray diffraction 10- 100 kvp 2 -100 ma
Tubes for these various purposes differ considerably in structure. Some of the tubes
now available are described in the following sections.
FIG. 2. JBasic .Clements oi an JL-ray Tube in Wi
Electrons are Ejected from a Hot Cathode Cby Therm-
ionic Action. (?, the glass envelope. A, the anode disk,
usually of tungsten. C, the cathode coil of tungsten
wire. S, the metal focusing shield connected electrically
to one of the cathode leads.
23. TUBES FOR X-RAY THERAPY
Roentgenologists require, for general x-ray therapy, tubes that will operate under the
following conditions:
1. Tube voltages of 50 to 400 kvp and tube currents of 2 to 30 ma (average), supplied
by constant-potential, full-wave pulsating, or half-wave pulsating high-voltage generators.
2. Exposures of 0.5 to 30 Tnin duration are used.
3. Insulation to rninirnize the hazard of electrical shocks to patient and operator are
essential.
4. X-rays must be confined to a cone the axis of which passes through the tube target
and the part of the patient's body to be treated, to minimise the possibility of x-ray burn
to the operator and patient.
The length of an x-ray tube depends upon the maximum anode-cathode voltage to
which it may be subjected. The ends of the tube, to which the electrical connections are
made, must be separated sufficiently to prevent sparkover. The electrical stress in the
glass envelope must be sufficiently low to prevent puncture. The tube must be mechani-
cally strong enough to support the anode and cathode assemblies rigidly. Therapy tubes,
for use at 50 to 400 kvp, immersed in oil, are 0.2 to 1.5 m long. Formerly the glass en-
velopes were made of soft glass. Manuf acturing methods devised recently have led to the
use of a hard glass such as Pyrex. Pyrex has superior heat-resisting qualities, greater
dielectric strength, and greater mechanical strength than soft glass. Air-cooled therapy
tubes have a spherical glass bulb, 15 to 25 cm in diameter, surrounding the anode and
cathode. This method of construction has the following advantages:
1. The sphere radiates more heat than a small cylindrical envelope.
2. The glass is far enough from the anode and cathode so that it is not stressed by strong
electric fields caused by the applied anode-cathode voltage.
4-84
ELECTRON TUBES
3. Stray electrons do not collect on the interior of the spherical surface in sufficient
quantity to cause unstable operation or puncture of the tube.
In the so-called Universal tube, Fig. 3, a bar of molybdenum 0.5 cm in diameter is
supported by glass at the end of the anode stem and extends into the tube, concentric
with its axis, to a point about 5 cm from the tube center. At this end of the bar a solid
tungsten block is fastened. This block is
truncated at an angle of 45° with the tube
axis. The minor axis of the elliptical face thus
formed is 2 cm long. The minor axis of the
target or focal spot is approximately 1.8 cm.
Fm.3. UnHersal TherapylTube, Solid Tung- Heat _ is dissipated chiefly by radiation A
sten Anode. Air-cooled. spherical glass bulb is required to aid this heat
dissipation.
The tubes with spherical bulbs are difficult to mount and to shield by reason of their
size. Modern therapy tubes are therefore designed for operation immersed in oil, with
cooling of the anode by means of oil that is forced against the back of the anode by a
pump. Special design of the electrodes, the use of hard-glass envelopes, and oil immersion
result in tubes that are considerably smaller than tubes designed for mounting in air. An
example of such a tube is shown in Figs. 4 and 5, designed to operate, in oil, at 250 kvp,
15 ma. Note the hollow cylindrical projection (hood) from the region of the tungsten
target toward the cathode; this hood prevents secondary electrons from impinging on the
inner surface of the glass envelope.
The cathode coil is usually a tungsten spiral which operates at 5 to 10 volts, 3 to 6 amp.
The coil is supported and surrounded by a metal cup to shield the glass from secondary
electrons and to focus the electron stream upon the target or focal
spot of the anode. In a therapy tube a small focal spot or source
of x-rays is not necessary. The focusing action of the cup is
limited to preventing electrons from going past the anode face
into the anode stem.
Tubes, such as that shown in Figs. 4 and 5, are often placed in
a grounded metal tube head, supported by means of a tube stand
that permits easy mechanical manipulation of the tube. High-
voltage leads are flexible shockproof cables with a grounded ex-
ternal sheath. Figure 6 shows an apparatus of this kind being
adjusted to make an x-ray film of a weld; therapy tube stands are
essentially similar. The tube head and the rectangular cone ex-
tending from the head toward the weld are lead lined; thus the
x-ray output is confined to a relatively sharply defined beam
through the cone.
All x-ray tubes used for the routine treatment of deep-seated
tumors are evacuated to a pressure of 10 "^ micron of mercury or
\
Steel
Cathode
Copper Hooded
Anode
Nickel Cooling
Coil
FIG. 4. X-ray Tube
Designed for Opera-
tion, Immersed in
Oil, at 250 kvp, 15
ma, Using Forced-
oil Cooling. (Cour-
tesy General Elec-
tric X-ray Corpora-
tion.)
Tungsten ,,,,,,
Window Ground Window In
BorosiUcate Glass
FIG. 5. Axial Section of Tube Shown in Fig. 4.
General Electric X-ray Corporation.)
(Courtesy
less. It is necessary not only to evacuate to this pressure while the anode and cathode
are cold but also to heat the metal parts by means of high-frequency induction while the
pumping proceeds. Before being sealed off, the tube is operated at an anode-cathode
voltage and current slightly in excess of the tube rating to insure thorough degassing of
the metal parts.
TUBES FOR X-RAY THERAPY
4-85
HIGH-VOLTAGE THERAPY TUBES. X-ray
apparatus for therapy and for industrial radiography
at tube voltages of 1000 and 2000 kvp are contained
in steel tanks, in which air or "Freon" is maintained
at a pressure equivalent to several atmospheres. The
source of high-voltage, mounted in the tank with the
x-ray tube, is a van de GraafT generator or a specially
designed transformer operating at 180 cycles per
second. The tubes are sealed, with the anode placed
at one end of the cylinder; the cathode is placed at
the other end. The anode is grounded, and the focal
FIG. 6. 220-kvp Shockproof X-ray Tubehead and Tube-
stand. (Courtesy X-ray Division, Westinghouse Electric
Corporation.)
spot is cooled by water that flows over the end of the
tube. A tube rated at 2000 kvp is shown in Fig. 7.
This tube has a gold target; there is some evidence
that the surface of the focal spot is molten during
operation, although there is no evidence of the in-
stability that might be expected to accompany this
condition. Note that the tube is equipped with a
series (180) of accelerating anodes. These are re-
quired to maintain uniform potential gradient along
the tube and to minimize the effects of electrons'
diverging from the beam. The magnetic focusing
coil shown in Fig. 7 insures stable size, shape, and
position of the focal spot on the gold target. The
tube is approximately 9 ft long; the extension from
the lowest accelerating anode to the target is 3 ft.
The rating is 2000 kvp, 300 juamp.; the focal spot,
with magnetic focusing, is approximately 2.5 mrn in
diameter.
2^-Cathode
Accelerating
Electrodes
.Focusing
Magnet
Water
-Cooling
Gold
/target
FIG. 7. Tube for Therapy and In-
dustrial Radiography; Operating
Voltage 2000 kvp. (Courtesy Mach-
lett Laboratories.)
4-86 ELECTRON TUBES
24. TUBES FOR MEDICAL ROENTGENOGRAPHY AND
ROENTGENOSCOPY
To produce diagnostically useful roentgenograms of parts of the human body, x-ray
tubes with the following characteristics are required:
1. The focal spot or source of x-rays must be as small as possible in order to obtain
sharp shadow borders.
2. The technique of roentgenography prescribes x-ray tube voltages of 30 to 110 kvp,
x-ray tube currents of 10 to 500 ma (average), and exposure times of 1/30 to 30 sec.
3. The primary x-ray beam must be confined to a cone with the focal spot at the apex
and the film at the base to protect the operator from x-ray burn.
4. Insulation of the tube and high-voltage leads is advisable but not necessary (except
in dental roentgenography) since the focal spot-film distances generally used are greater
than 60 cm.
Except for the requirement that the focal spot be small, the same principles are applied
in designing roentgenographic tubes as those described above for therapy tubes. The
need for minimizing the focal spot size having been prescribed, certain practical factors
are found to oppose this decrease:
1. For any particular method of anode construction the energy dissipated at the focal
spot during an exposure cannot exceed the value which will melt the tungsten target.
The melting point of tungsten is 3370 deg cent.
2. Owing to the thickness of the part to be roentgenographed, the shadows of parts
farthest from the film are more distorted than those near the film. The focal spot-film
distance must be increased to decrease this effect. The energy supplied to the tube in-
creases in proportion to the square of the focal spot-film distance. Therefore, the focal
spot area must be increased in like proportion. In other words, if the focal spot-film dis-
tance is increased to reduce the magnification of shadows of parts at a distance from the
film, the focal spot must be enlarged, the energy supplied to the tube must be increased,
and the sharpness of the shadows remains unchanged.
3. Parts of the body are continually in motion. Roentgenograms of such parts must be
made in as short a time as possible to minimize the unsharpness or blurring caused by
motion during exposure. The minimization of exposure time requires an increase in focal
spot size, all other factors remaining constant. For example, roentgenogram of the chest
of a cadaver may be made with a tube having a focal spot less than 1 mm square. To
make a roentgenogram of the chest of a normal adult requires a tube with a focal spot at
least 3 mm square. Even this is a compromise, for no matter how short the exposure time
some unsharpness is produced by motion.
Nearly all roentgenographic tubes now manufactured are constructed and used so that
the line from the focal spot to the center of the film makes an angle of 10° to 45° with the
anode face. The projection of the actual focal spot (the source of x-rays) upon a particular
point in the film is called the effective focal spot area at that point. Figure 8 illustrates
three types commonly used. The effective focal spot Fz for the 45° tube is a circle 6 mm
in diameter. The effective focal spots for the 20° and 10° tubes having the same target
areas as the 45° tube are squares with sides of 3.7 mm and 2.6 mm, respectively. The max-
imum allowable exposure energies (for exposure times less than 0.2 sec) are equal for the
three tubes, since the actual focal spot areas are equal. Therefore, for a given maximum
rating the sharpness of the roentgenographic image increases as the angle between the
focal spot and central x-ray beam decreases. Two limitations prescribe the minimum
focal spot-film distances at which a tube may be used:
1. The intensity of x-rays emanating from the focal spot within a few degrees of the
tangent to the anode face is less than the intensity of the central beam at the same dis-
tance from the tube. The intensity must be practically uniform over the area of the x-ray
film, in the absence of absorbing objects between tube and film.
2. The effective focal spot size and the distortion vary over the film area. This varia-
tion must be minimized to insure that the roentgenogram is diagnostically useful over its
entire area.
The design of roentgenographic tubes is determined in general by the criteria described
above in article 23, "Tubes for X-ray Therapy." There are three requirements which
differ qualitatively:
1. The anode-cathode voltages are less for roentgenography than for therapy.
2. It is extremely important to produce a small, uniform effective focal spot in roent-
genographic tubes.
3. Exposure times for roentgenography are relatively short, requiring that the anode
have a high heat capacity.
TUBES FOR MEDICAL ROENTGENOGRAPHY
4-87
Modern roentgenographic tubes use the line or band focus shown in the 20° and 10°
sketches, Fig. 8. The target is a disk of tungsten about 1.5 mm thick, usually with an
area two or three times the actual focal spot area. The tungsten is embedded in a heavy
copper bar. Suitable thermal contact between the tungsten and copper is difficult to
obtain. The usual procedure involves fixing the tungsten disk at the bottom of a graphite
crucible and pouring molten electrolytic copper over the disk. The casting is accomplished
A— Anode
B=X-ray Film
Fi=ActuaI Focal Spot
F2= Effective Focal Spot
•1
FIG. 8. Relations of Actual Focal Spots, FI, and Effective Focal Spots, F%, for Roentgenographic Tube
Anodes. Actual focal spot areas of all three tubes are equal.
in an evacuated chamber to prevent the formation of any compounds that might prohibit
the adherence of the copper to the tungsten.
With the type of construction just described, the maximum allowable exposure rating
for exposures of 1 sec or less is 250 watts per square millimeter of actual focal spot area.
For long exposures the rating depends upon the efficiency of the heat-radiating system,
and therefore it is specified for each type of tube by the manufacturer. These data are
given in graphical form, called tube rating charts.
Shock-proof roentgenographic tubes are constructed similarly to the therapy tube
shown in Fig. 6.
To increase the rating for a focal spot of a given size, tubes have been developed with
rotating anodes, the cathode stream being so directed that the focal spot is separated
several millimeters from the tube axis. Different areas of the rotating anode therefore act
as focal spot during the exposure. Two such tubes are shown in Figs. 9-12. The anode
FIG. 9. Rotating-anode Roentgenographic Tube. Ratings (in oil-insulated tubehead): 2-ram focal
spot, maximum voltage 100 kvp, 500 ma at 90 kvp for 1/30 sec, 400 ma at 80 kvp for 1/5 sec; 1-mm focal
spot, maximum voltage 100 kvp, 200 ma at 90 kvp for 1/20 sec, 100 ma at 90 kvp for 3 sec. (Courtesy
Machlett Laboratories.)
within the evacuated tube envelope operates as the rotor of a split-phase induction motor.
These tubes are equipped with two cathodes; one produces an effective focal spot 1mm
square; the other, 2 mm square. The rotors operate at approximately 3000 rpm.
The tube shown in Figs. 9 and 10 is equipped with an anode comprising a tungsten disk
approximately 6 cm in diameter and 2.3 mm thick. This disk is mechanically connected
to the rotor of the driving motor by means of a short molybdenum shaft; the entire assem-
ELECTRON TUBES
bly is blackened to promote radiation of heat to the oil surrounding the tube when it is
operating in its shockproof tube head. The balls of the bearing within the vacuum tube
are coated with a thin, uniform film of silver, which
reduces bearing friction. Samples of the manufac-
turer's ratings are listed below Fig. 9.
The anode structure of the tube shown in Figs. 11
and 12 consists of a tungsten cap backed by a heavy
copper blackened cylinder, the purpose of which is to
provide high heat storage and a large area for the
radiation of heat to the oil surrounding the tube en-
velope. The ball bearings of this tube are lubricated
by thin films of barium.
FIG. 10. Section of Rotating Anode
Tube Shown, in Fig. 9. (Courtesy
Machlett Laboratories.)
FIG. 11. Rotating-anode Roentgenographic Tube.
Ratings (in oil-insulated tubehead): 2-mm focal
spot, maximum voltage 100 kvp, 500 ma at 90 kvp
for 1/30 sec, 400 ma at 80 kvp for 2/5 sec; 1-mm focal
spot, maximum voltage 100 kvp, 200 ma at 94 kvp
for 1/20 sec, 100 ma at 90 kvp for 5.6 sec. (Cour-
tesy General Electric X-ray Corporation.)
Borosilicate
Glass
Insulating
Shield
Stator
Rotating-anode tubes are usually equipped with counters to record the number of
exposures, and with control circuits that prevent high-voltage excitation of the tube unless
the anode is rotating at rated speed
(approximately 3000 rpm) .
Tubes used for roentgenoscopy (view-
ing of x-ray shadows by means of a
fluorescent screen) are similar to the
stationary-anode tubes described above,
except that focal spots less than 2 mm
square may be used, since the current
seldom exceeds 10 ma. These tubes are
often non-shockproof, since they are
commonly mounted under a fluoroscopic
table, out of reach of operator and
patient.
Modern roentgenographic and fluoro-
scopic tubes should be used about 10-20
Steel
Tungsten
Copper Anode and
Rotor Housing
Blackened Surface
FIG. 12. Section of the Rotating-anode Tube Shown
in Fig. 11. (Courtesy General Electric X-ray Corp-
oration.)
per cent below the manufacturers'
ratings to guarantee a long useful life.
Roentgenographic tubes, so operated,
often can be used for 100,000 exposures
or more.
BIBLIOGRAPHY
4-89
25. TUBES FOR INDUSTRIAL ROENTGENOGRAPHY
AND FLUOROSCOPY, AND FOR X-RAY DIFFRACTION
The use of x-rays (and of gamma rays) for the examination of commercial products has
greatly increased, particularly during World War II; such examinations are quick and
non-destructive. The following are representative of the diverse applications of this
method of inspection: the examination for flaws in castings and welded joints; the inspec-
tion of packaged foods for foreign bodies; the final checking of manufacturing tolerances
in such items as golf balls and multielectrode vacuum tubes; the inspection of packages for
contraband; the inspection of citrus fruits suspected of being damaged by frost; the in-
spection of paintings and mummies.
X-ray tubes for industrial radiography and fluoroscopy are similar to those described
in articles 23 and 24. The desire to use x-ray tube voltages up to 2 Mv for radiography of
thick (as much as 0.3-0.4 m) steel was, in fact, a major stimulus to the development of
the high-voltage tubes described in
article 23 (Fig. 7) . In all industrial
radiographic tubes, regardless of
voltage, as small a focal spot as
possible must be produced to mini-
mize the unsharpness of shadow
borders, just as in medical roent-
genography.
FIG. 13. Shockproof X-ray Diffraction Tube, with Grounded,
Water-cooled Anode of Molybdenum, Copper, Cohalt, or
Iron, and a Window of Beryllium. Eatings 50 kvp, 10-20
ma, continuous. (Courtesy Machlett Laboratories.)
Since industrial radiographic equipment may have to be moved about in a factory to
use it near a heavy object to be inspected, design of equipment is based upon movabUity,
flexibility of adjustment, and adequate protection of personnel from electric shock and
excessive exposure to x-rays. Thus all industrial radiographic apparatus now manufac-
tured is shockproof and shielded with lead or other x-ray-absorbing material, except in
the direction of the useful beam.
The investigation of the structure of crystalline materials by means of x-ray diffraction
has been developed from the early (1908-1915) theoretical analysis and experiments of
von Laue, Friedrich, Knipping, W, H. and W. L. Bragg, and their colleagues. In recent
years, x-ray diffraction apparatus suitable for routine analyses of crystal structure has
been used in industry. X-ray tubes for this purpose consist of an anode of tungsten,
molybdenum, copper, iron, or cobalt, a conventional incandescent tungsten cathode, and
one or more windows of beryllium, which has an extremely low x-ray absorption coefficient.
FIG. 14. Section of X-ray Diffraction Tube Shown in Fig. 13. (Courtesy Machlett Laboratories.)
The tubes operate at 10-50 kvp, 10-50 ma. A selective filter may be used to isolate the
characteristic radiation from the anode, thereby producing a relatively intense, almost
monochromatic beam of x-rays. A photograph of an x-ray diffraction tube and a cross-
Bection of the tube are shown in Figs. 13 and 14.
BIBLIOGRAPHY
1. Kaye, G. W. C., X-rays, Longmans, Green (1926).
2. Coolidge, W. D., A Powerful Roentgen-Ray Tube with a Pure Electron Discharge, Phys. Rev.,
Vol. 2, 409 (1913).
3. Langmuir, Irving, The Effect of Space Charge and Residual Gases on Thermionic Currents in
High Vacuum, Phys. Rev., Vol. 2, No. 6 (December 1913).
4. Bouwers, A., An X-ray Tube with Rotating Anode, Physics, Vol. 10, 125 (1930).
5. St. John, A., and H. R. Isenburger, Industrial Radiography, 2nd Ed. John Wiley (1943).
6. Siegbahn, M., The Spectroscopy of X-rays. Oxford University Press (1925).
7. Clark, G. L., Applied X-rays, 3d Ed. McGraw-Hill (1940).
8. Slack, C. M,, and L. F. Ehrke, Field Emission X-ray Tube, J. Applied Phys., Vol. 12, 165-168
(February 1941).
9. Machlett, R. R., and T. H. Rogers, A New Design for Increasing the Heat-dissipating Capacity
of Rotating Anode Tubes, Am. J. Roentgenology & Radium Therapy, Vol. 48, 685-690 (November
1942).
10. Atlee, Z. J., Design and Application of X-ray Tubes, Electronics, Vol. 13, 26-30, 62, 64 (October
1940).
SECTION 5
ELECTRIC CIRCUITS, LINES, AND FIELDS
THEORY OF LINEAR PASSIVE NETWORKS
ART.
BT p- H- RICHARDSON
PAGE
1. Non-sinusoidal Currents and Voltages. . 02
2. Single-mesh Circuit .................. 03
3. The Complex Frequency Plane ........ 04
4. Mesh Equations ..................... 05
5. Nodal Equations ..................... 06
6. Two-terminal Impedances ............. 07
7. Four-terminal Networks .............. 10
8. Power Transfer ...................... 15
9. Distortion ........................... 16
10. Corrective Networks ................. 16
RECURRENT NETWORKS
BT P. H. RICHARDSON
11. Symmetrical Networks .............. 23
12. Uniform Lines — Networks with Distrib-
uted Constants .................... 24
TRANSIENTS IN NETWORKS
BY HAROLD A. WHEELER
13. Transient Disturbances ............... 26
14. Behavior of Networks ................ 29
15. General Principles .................... 33
NON-LINEAR ELECTRIC CIRCUITS
BT KNOX MclLWAiN
16. Power Series Solution ................. 38
17. Trigonometric Series ................. 39
ART. PAGE
18. Inductance Variation 40
19. Capacitance Variation 41
20. Approximate Series Expansion for the
Plate Current of a Triode (Assumes
it Constant) 41
21. Characteristics of Triode with Load 42
22. Analysis for Multi-electrode Tubes 45
23. Method of Successive Approximations . . 45
24. Harmonic Analysis of the Current for a
Sinusoidal Applied Voltage 46
25. Input Impedance of a Triode 49
ELECTROMAGNETIC RADIATION
BT KNOX MclLWAiN
26. Maxwell's Equations 50
27. Progressive Plane Waves 51
28. Fields Due to a Current in a Wire 52
29. Reflection and Refraction 52
ELECTROMECHANICAL SYSTEMS
BT KNOX MclLWAiN
30. Energy of Mechanical and Electrical
Systems 57
31. Vibrations of a System of One Degree of
Freedom 58
32. Comparison of Mechanical and Electrical
Systems 59
33. Electromechanical-acoustic Systems .... 62
5-01
ELECTRIC CIRCUITS, LINES, AND FIELDS
THEORY OF LINEAR PASSIVE NETWORKS
By P. H. Richardson
The networks to be considered are assumed to consist of resistances, inductances,
capacitances, and mutual inductances connected or coupled together in some manner.
The problem is to determine the steady-state response of the network to an impressed
voltage, or current, of any complexity. It is presupposed that the driving voltage has
been impressed on the network at a time far enough in the past to have permitted any
transients to die out.
To facilitate the solution of the problem the following assumptions are made:
1. The impressed voltage is periodic.
2. The network is linear. The values of the component elements are independent of
the current through them.
3. The network is passive. There are no sources of energy interior to the network, and
no energy is dissipated other than by the resistance elements of the network.
1. NON-SINUSOIDAL CURRENTS AND VOLTAGES
As a consequence of the linearity of the networks the coefficients of the differential
equations are real constants. The equations express the equilibrium conditions which
exist between the instantaneous driving voltages
^ ^Jx^ "n and *ne countervoltages in the circuit. For ex-
ample, in the circuit of Fig. 1, consisting of R, L,
and C (= 1/D) in series, the differential equation is
00
FIG. 1. Single-mesh Circuit where q is the charge on the condenser, and
i — dq/dt. If <ji is the charge corresponding to an
impressed voltage ei, and 32 is the charge corresponding to an impressed voltage eg, it is
evident that
and
d^qz dQz
L ~~~~ "~f~ R ~ — ~}~ DQ% == ^2
By simple addition it follows that
L ^(Qldp g2) + R ^ti ^ + Dfa + &> - e> + e* <2>
Thus, for a linear network the principle of superposition holds. In other words, the
current (or voltage) at any point flowing in response to several driving voltages acting
together is the sum of the currents (or voltages) at that point which would flow in response
to the driving voltages acting separately. This principle is of major importance in network
analysis.
FOURIER'S THEOREM. A second important concept in the analysis of the steady
state is Fourier's theorem, which states that any single-valued continuous periodic func-
tion can be expressed as an infinite series of sine waves. In particular, if f(x) is a function
which is finite in the interval from — c to +c and has only a finite number of discontinuities
in that interval, then for any value of s in the interval
f, , OQ . TTX , 27TX ,
f(x) = — + ai cos h 02 cos h • • •
, - . 7TX , , . 2TTX , ,„
+ 6:801 1-62 sin h • • • (3)
c c
5-02
SINGLE-MESH CIRCUIT 5-03
where the coefficients oo, ai, as, • • • 61, 62, • - • are determined as follows:
1 rc „ . mrx 1 re . TITHE _
an = ~ / /(») cos - efo; 6W = - I /(x) sin - da;
CJ—C C C J —c C
Or, equivalently,
A*) - f + ^isin (y + ft) + A2sHi p?p + ft) + .•• (4)
where
A proof of this theorem will be found in any standard book on calculus.
This theorem, taken in conjunction with the principle of superposition, makes it pos-
sible to obtain the response of a linear network to a periodic voltage of any complexity,
provided that a solution is available for the case in which the driving voltage is a simple
sinusoid. The complicated wave form of the impressed voltage is first resolved into its
component sine waves, the solution of the equation is obtained for each component, and
the solutions are added to obtain the final current or voltage required.
2. SINGLE-MESH CIRCUIT
Before proceeding to the general problem it will be profitable to examine in detail the
response of the single-mesh circuit of Fig. 1. As already noted the differential equation is
(5)
air at
where the complex exponential form has been written for the impressed voltage. The
notation is the usual one, where a? == 2-jrf, f — frequency in cycles per second, EQ is a
constant, either real or complex, and y — V— 1.
Assuming a solution of the form q = qoept leads to the result that
(Lp2 + Rp + D^qoeP* = E«0»* (6)
which is evidently a solution provided that p — ju. Then
go :
and
+ Rp + D
where IQ ~ Eo/Z, Z = R + Lp + D/p, and p = ja.
Upon substituting ju> for p the result is the familiar one that
*'-|-V«« (8)
Zi
where Z — R 4- jx and x — (Leo — !>/&) -
The use of the complex exponential form for the impressed voltage converts the
differential equation at once to an algebraic equation. The resultant current is a complex
exponential form of the same frequency as the impressed voltage. The impressed voltage
is made up of two components in quadrature, and the resultant current is also made up
of two currents in quadrature. Since the coefficients of eq. (5) are real, it is evident that
the response to a real voltage is also real, while the current in response to an imaginary
voltage is imaginary. Consequently, by the principle of superposition, the physical
current flowing in response to a voltage EQ cos co£ is given by the real part of eq. (8) .
The imaginary part of the current, with the / discarded, is the physical current that
flows in response to an impressed voltage EQ sin ut. Hence
and
%nag - T-T sin (tat -f a — j8)
5-04
ELECTRIC CIRCUITS, LINES, AND FIELDS
where Z = | Z \ /g, EQ = | EQ \ /a, and 0 « tan"1 (a;/B) . The quantity | EQ \ is the
maximum value of et and similarly | Io | is the maximum value of i. By proper choice
of units | EQ | may be the rms voltage, and then | Jo | is the rms current. Hence the ratio
| EQ/IQ I becomes the absolute value of the steady-state a-c impedance. The complex
quantity Z — e/i — EQ/!Q is denned as the complex steady-state impedance and may
be studied as a function of p = jco.
3. THE COMPLEX FREQUENCY PLANE
The definition of the parameter p = j2irf can be usefully extended for analytic purposes
to situations in which / and p are complex. Suppose a voltage E^cF* is assumed where
o | /« and p = pi + jpz. Then
Eo^ = | EQ | e*)iie7'^2*+a> ' (10)
In accordance with the above discussion the physical voltage is taken as the real part of
this, which is a sinusoidal oscillation with positive or negative damping depending on pi.
The corresponding steady-state physical current is obtained by dividing the complex
voltage by the impedance and taking the real part of the result. This is a damped sinusoid
of the same frequency and damping as the voltage.
Complex frequencies can be represented on a plane as shown in Fig. 2. The horizontal
axis represents real values of p, and the vertical axis imaginary values of p, or real values
1 8
-Real p Axis
p plane
+ Real p Axis
If
,33
/R/ Y
position of
v2Ly
PI
3?2
0
A
A'
+CO
1
<D/L
B
B'
p plane _^J
= D/L
G
C
B ,'
>D/L
D
D'
,°
/
^ 1
+ P
D'
~°\ D
\
FIG. 2. Complex Frequency Plane
FIG. 3. Distribution of Zeros and Poles
in Complex Plane
of frequency. In network analysis a distinction of primary importance is made between
the right and left halves of the p plane, since on the left half-plane the voltages and currents
correspond to functions which decrease exponentially with time, whereas on the right half-
plane they increase exponentially with time. There is a close connection between the
steady-state characteristics of a network and its transient response. Since a network
whose transients increase with time is unstable, the characteristics of physical networks
in the right half-plane are necessarily limited. There is no such distinction between the
upper and lower halves of the plane.
As an illustration of this discussion consider the impedance of the single-mesh network
of Fig. 1, Here the impedance
T / r> n\
(ID
where
- (P ~ Pi) (P - 22)
R
are the zeros of the impedance expression. They are seen to be real when (B/2L)2 ^ D/L,
while they are conjugate complex numbers when (J2/2I/)2 < D/L. The locations of the
zeros pi and pz are indicated on Fig. 3 as R/L is varied and D/L is held fixed. It should
be noted that the values of pi and p% always have negative real parts; they are always in
the left half-plane. The impedance becomes infinite, that is, it has a pole, when p is zero,
MESH EQUATIONS
5-05
as represented by the cross at the origin. A second pole occurs at infinity where the im-
pedance again becomes infinite.
4. MESH EQUATIONS
The response of a complicated network of the type shown in Fig. 4 is determined by
making use of the equilibrium conditions which must be satisfied by the instantaneous
currents and voltages. There are several methods of writing the equations; one uses
branch equations, a second mesh equations, and a third nodal equations. In writing
branch equations the current in each branch, ZIQ, Z&, etc., is separately specified, and the
sum of the instantaneous voltages in
each branch is equated to the volt-
age applied to the ends of the branch.
There are B such equations, where B is
the number of branches. At each node,
or junction point between branches,
the sum of the currents entering the
node must be equal to the sum of the
currents leaving the node. Therefore,
J relations of this kind can be found,
where / is the number of junction
points. If there are S separate parts
(not conductively connected to one
another, as mesh 7 in Fig. 4) only
J — S of these equations are useful,
since, if the law of the conservation
of charge is satisfied at all but one node
in each of the S parts, it is automat-
ically satisfied at the last one also.
There are then B 4- J — S independ-
ent equations.
The original branch equations in-
clude, in addition to the B branch currents, only differences in the node voltages. S of
these can be arbitrarily assumed, and there will remain exactly B -f- J — S unknowns
to be determined.
By adding together the branch voltage equations around a complete loop, or mesh, and
eliminating the superfluous branch currents by means of the nodal current equations, an
equation is found for each mesh. A similar equation can be found for each of the N
meshes of the network, where N = B — J + S.
A considerable simplification can be achieved by originally specifying only one current
for each mesh of the network as shown in Fig. 4. By choosing circulating currents the
nodal equations are automatically eliminated, as are the voltage differences which appear
in the branch equations. The minimum number of mesh currents that can be used is,
of course, B — J + S. For example, in Fig. 4 there are 15 branches, 10 junctions, and 2
parts, hence 7 meshes. It is important to note that a closed loop, consisting of a single
branch with its two terminals coinciding, is considered to have one junction.
By adopting a set of conventions, regularity of notation is introduced into the equations.
Those generally used are that all currents are assumed clockwise; branches common to
two meshes a and b will carry as subscript the symbols of both meshes, as Za&; branches
appearing in one mesh only will be designated Za^\ and the sum of all the branches in a
particular mesh will be designated as Zaa- In computing Zaai the self-impedance of a
mesh, all the self-inductance in the mesh is included but mutual inductances to other
meshes are not.
Then for any linear network of N meshes a set of N equations is found as follows:
2 70
FIG. 4. Multi-mesh Network
Zu.Ii + ^12/2 +
Zzil* + #22/2 + #23/3
' Zinln
(12)
where each of the Z's is of the form
Zab =
and p and 1/p represent differentiation and integration with respect to time.
5-06
ELECTRIC CIRCUITS, LINES, AND FIELDS
The mesh equations developed thus far have represented the differential equations of
the circuit. The set of differential equations is transformed to an identical set of algebraic
equations by the assumption made in article 2, that each of the sinusoidal voltages and
currents can be written as E^ or ldwt, where E and I are constants, co = 2irf, f = fre-
quency in cycles per second, and j = V — 1. This transformation results from the fact
that differentiation and integration of e>ut replaces each p in eq. (12) by ju. The time
factors 6»'w* appear on both sides of the equation and can be divided out. The Z's are
then the complex self- and mutual impedances of the meshes. And the 7's and 28* & are
regarded as representing merely the constant coefficients in the more general expressions
JVW* and E^.
DRIVING POINT AND TRANSFER IMPEDANCES. The determination of any
particular current flowing in response to a particular voltage is equivalent to the solution
of a set of ordinary linear equations. The current in the first mesh flowing in response to
the voltage Ei^wt, also in that mesh, is given by the method of determinants (see Handbook
of Engineering Fundamentals, Eshbach, John Wiley) as
where A is the determinant of the coefficients in the left-hand side of eq. (12) and AH
is the determinant obtained by omitting the first row and first column of A. The driving
point impedance in the first mesh is by definition the ratio of the voltage to the current
in eq. (13). Thus
In similar fashion the current in the second mesh flowing in response to the voltage
in the first mesh is given by
(15)
where Ai2 is the minor of A obtained by removing the first row and second column. The
transfer impedance from the first to the second mesh is defined as
(16)
It should be noted also, since in a passive network Zab = Z&a, that
, * _* A
6. NODAL EQUATIONS
An analogous system of equations can be set up in terms of driving currents at the
nodes and nodal voltages. In this analysis the
fundamental equations are conditions of current
equilibrium. In the circuit of Fig. 5, Ii, /2, /a, and
/4 are the driving currents, and FH, Fi2, FIS, etc.,
are the admittances (reciprocal impedances) of the
various branches. Node 4 has been assumed at
ground potential. At node 1, then,
(18)
where FU = FW •+• Fi2 + FIS is evidently the sum
of the admittances of all the branches connected
to l ™ih aU the other nodes connected together.
FU is therefore a self-admittance analogous to the
self-impedance in the mesh analysis. Similarly
FIG. 5. Illustration for Method of Nodal
Analysis
and FIS are mutual admittances analogous to mutual impedances.*
* For a treatment of nodal analysis for circuits involving mutual inductance the reader is referred
to Gardner and Barnes, Transients in Linear Systems, VoL I.
TWO-TEEMINAL IMPEDANCES 5-07
In any conductively united network having / nodes a set of J — 1 independent equa-
tions of the above form can be written. The complete set becomes
Ii
J2 (19)
+ YnnEn - In
where the F's are of the form
Yab - Cabp + 0B6 + -L . I
Lab P
and p and 1/p have the meanings previously ascribed to them.
A solution of the set of nodal equations to find the steady-state voltage corresponding
to a given set of sinusoidal driving currents can be obtained by the processes already used.
The driving point admittance Y between the first node and ground is defined as
where the primes indicate that the A's refer to the set of equations (19).
Similarly the transfer admittance between the first and second nodes is defined as
»-$--£
In this case, also, since Yab — Yba,
**-*--£--£
One consequence of the analogy between the mesh and nodal equations is that the
selection of one of the two methods of solution in any particular problem is entirely a
matter of convenience. The symmetry of the two methods is further emphasized by the
equivalence of Fig. 6, in which a constant-voltage generator in series with an impedance Z
is shown as replaceable by a constant-current genera-
tor in parallel with an impedance Z.
A second consequence of the analogy leads to the
principle of duality in network theory. The symmetry
in the current and voltage methods of analysis in-
cludes the individual terms in the equations. The
general term Zab of eq. (12) is replaced by Yab of eq.
(19) if
Lab — Cab, Rab ss Gab and Dab — ( 73 — I — ^ —
\Cab/ Lab
Consequently a set of nodal equations can be obtained
identical with a given set of mesh equations by inter-
changing r and g, and L and C, wherever they appear. For every impedance function,
therefore, there is a corresponding admittance function. If the mesh equations for one
network correspond, term by term, with the nodal equations for another, the two networks
are called inverse structures, or duals.
6. TWO-TERMINAL IMPEDANCES
The driving point impedance, or admittance, of a network can be expressed as the ratio
of determinants whose elements are relatively simple functions of p = ju>. In the mesh
system the general impedance coefficient can be written as Z0& — LabP + -Ka& + Dab 1/3?-
Since the terms A, An, and Aaa used in defining driving point impedances can be ex-
pressed as products of terms of this type, it follows that they are polynomials in p dividad
by some power of p. That is,
Bnpn + Bn-ip"-1 + • - • + B1P + Bo
Put in terms of the zeros and poles the expression is
_ Am(p - pi)(p - #2) • • • (p - pm)
(24)
5-08 ELECTRIC CIRCUITS, LINES, AND FIELDS
where ordinarily the pa's are all different. Note that the pa's and pa"s, are the roots of the
polynomials in the numerator and the denominator. In special cases two or more zeros
or poles may coincide. The zeros and poles may be thought of as corresponding to the
resonances and antiresonances of purely reactive networks except that they may occur at
complex frequencies.
RESTRICTIONS FOR PHYSICAL REALIZABILITY. A passive two-terminal or
driving point impedance is subject to the following restrictions:
1. In terms of the frequency variable p — jco the zeros and poles are either real or they
occur in conjugate complex pairs.
2. The real and imaginary components are respectively even and odd functions of
frequency on the real frequency axis.
3. None of the zeros and poles can be found in the right half of the p plane.
4. Zeros and poles on the real frequency axis must be simple.
5. The real component of the driving point impedance cannot be negative at real fre-
quencies.
General methods for finding physical networks corresponding to any impedance func-
tion meeting these restrictions have been devised.* A method due to Brune depends on
the fact that the minimum value of resistance, or conductance, at real frequencies is less
than any value in the right half-plane. If the function is diminished by a real positive
constant equal to the minimum value of the resistance, the remainder corresponds to a
passive impedance having a zero resistance at a real frequency. This remainder is termed
a minimum resistance, or minimum conductance expression. Similarly it can be shown
that an impedance expression having zeros or poles on the real frequency axis can be
diminished by the reactance, or susceptance, corresponding to its real frequency zeros and
poles. An impedance having no poles at real frequencies is called a minimum, reactance
expression, while one having no zeros at real frequencies is called a minimum, susceptance
expression. If an impedance is both minimum resistance and minimum reactance, there
is a unique relation between the resistance and reactance; if either is known at all fre-
quencies the other can be determined.
NETWORKS OF PURE REACTANCES. If it is specified that the zeros and poles of
an impedance expression occur at real frequencies, or imaginary values of p, the form
of the impedance expression becomes
~ P22)(P2 ~ P42) • ' ' (P2 ~ Pm2) , .
=
(P2 ~ Pi2) (P* ~ P32) ' • ' (P* ~ Pm-fi
where k is a positive real constant, while pi2, p22, etc., are negative real quantities. Each
of the factors represents a pair of zeros, or poles, at positive and negative real frequencies.
The zeros and poles are restricted in that
- Pm2 ^ ~ Pm-l2 ^ ~ ' - ' ^ ~ P22 ^ ~ Pi2 ^ 0 (26)
or the zeros and poles must alternate.
As written the impedance is specified as an inductive reactance at both zero and infinite
values of frequency. To obtain complete generality it must be allowable to specify
p^ = o (which introduces a pole at p = 0), or that the factor p2 — pm2 can be omitted
(which leads to a zero at infinite frequency) .
It has been demonstrated f that the impedance of eq. (25) corresponds to a physical
network containing only inductances and capacitances. The network can be found either
representing the poles as antiresonant net-
I-MTOQT> | - qnnp 1 works in series or by representing the zeros as
JL _L _J_, resonant networks in parallel. For a detailed
~T "T ~T ~T" discussion of these impedances see Section 6,
, s -^- _u_ _j_ __i_ resonant networks in parallel. For a detailed
(a) T T T T<
Article 17.
The reactive networks can also be realized
in other configurations of which Figs. 7a and
76 are typical. These are obtained as the re-
sult of continued fraction expansions in which
the zeros and poles at zero and infinite frequency
are removed alternately.
FIG. 7. Ladder-type Reactive Networks c^e o the restrictions on the zeros and
poles the impedance characteristics of reactive
networks are necessarily restricted. The slope of the characteristic is always positive and
necessarily greater than that of a simple inductance or capacity having the same reactance
at a given frequency.
* Brune, Journal of Mathematics and Physics, M.I.T., Vol. X, October 1931, pp. 191-235. Darling-
ton, Journal of Mathematics and Physics, M.I.T., Vol. XVIII, No. 4, September 1939, pp. 257-353.
tR. M. Foster, A Reactance Theorem, B.S.T.J., April 1924, pp. 259-267.
TWO-TERMINAL IMPEDANCES
5-09
NETWORKS OF RESISTANCES AND INDUCTANCES OR RESISTANCES AND
CAPACITANCES. Very similar to the purely reactive networks wliich result when the
zeros or poles are specified at real frequencies, a simple series of networks results when it
is specified that the zeros and poles occur at imaginary frequencies, or real values of p.
Again only two kinds of elements, either resistances and inductances or resistances and
capacitances, are required to realize such impedances.
If the expression corresponds to a network of resistances and inductances, it is of the form
kp(p —
• • > (p —
• • • (p -
(27)
and | Z | increases as p increases. If, on the other hand, the expression corresponds to a
network of resistances and capacitances | Z \ decreases as p increases. An alternative
form for Z is
k(p — 02) (p — ai) - • • (p — am) .
~ - ~ - - -
~,
— ai)(p —
— Om-l)
In both expressions the zeros and poles occur alternately and ai, 02, etc., are negative real
quantities or zero.
As in the case of the reactive network the impedances may be represented in partial
fraction form. For example, the impedance of eq. (28) can be expanded in the form
Z «
P —
,
• -r "
p —
Dm-l
(29)
where Da = [(p — aa)Z]p=aa and R is the resistance at infinite frequency. Each of the
terms Da/(p — aa) is identifiable with the parallel combination of resistance and capaci-
tance, where ra — — Da/aa and Ca = I/At-
INVERSE OR RECIPROCAL IMPEDANCES. The duality between the impedance
and admittance methods of analyzing a network suggests the possibility that to every
network there corresponds an inverse. The requirement that the real part of an im-
pedance be positive is merely another way of stating that the real part of the corresponding
admittance be positive. Also, the restrictions on the zeros and poles are identical, so that
the interchange of zeros and poles when an impedance is replaced by its reciprocal does
not change the conditions for physical readability. It follows, then, that, if a passive
impedance is physically realizable, its reciprocal is also.
^ The reciprocal impedance for the structure of Pig. 8a is found, for example, as follows:
1. Each series connection is replaced by a parallel connection, and vice versa.
2. The individual resistances, inductances, and capacitances are respectively replaced
by resistances, capacitances, and inductances in such a way that
The structural inverse of Fig. 8a is therefore given by 86. This process is evidently not
general since it considers only series and parallel connections. An extension of the method
FIG. 8. Inverse Two-terminal Networks
FIG. 9. Inverse Bridge Networks
depends on a consideration of the geometry of the network. The branches of the network
are considered as lines between the junction points, dividing the plane of the diagram into
5-10
ELECTRIC CIRCUITS, LINES, AND FIELDS
areas. The process consists of interchanging areas and points. A new point is taken
interior to each area and is connected to each similar point by a branch inverse to the
branch separating the areas. The inverse of a bridge network is found by this process
to be another bridge, as shown in Fig. 9. Even this process is not entirely general.*
COMPLEMENTARY IMPEDANCES. In addition to the inverse of a given impedance
function one can also speak of its com-
plement. The complement is denned by
the requirement that the sum of the
original impedance and its complement
is a real constant. The complement of
a passive impedance can be found if the
prescribed impedance has no poles on
the real frequency axis, and if the sum
of the impedance and its complement is
chosen at least as great as the maximum
value of the resistance of the original impedance. The constant resistance combination of
Fig. 10 represents a simple example of the relationship.
when — =-
FIG. 10. Complementary Impedances in Series
7. FOUR-TERMINAL NETWORKS
The four-terminal network, or two-terminal pair, is a special form of general network
of major importance. The external characteristics of the network are completely specified
in terms of Ii, EI, /2, and E% of Fig. 11. A solution is ob-
tained from eq. (12) with the assumption that all voltages ll - 2
except EI and E% are zero. Thus 1 <;
An
—
A22
__
(30a)
(306) Fia. 11. General Four-terminal
Network
Or, solving explicitly for EI and E%, and noting that AAn22 = AnA22 — Aig2
EI = — /i + -^- 12 (31a)
Ez = — I + An I2 (316)
The currents of eqs. (30) are determined by the voltages EI and E% and the quantities
An/A, A22/A, and — Ai2/A.
DRIVING POINT AND TRANSFER IMPEDANCES. The physical significance of
the ratios is seen by successively setting Ez and EI equal to zero. Thus
-^ = Ysi = admittance at terminals 1-1' with 2-2' shorted
22
— = Yaz = admittance at terminals 2-2' with 1-1' shorted
— — M
YS2i ~ transfer admittance from either end with the opposite end shorted
Similarly, if 1$ and Ji of eqs. (31a) and (316) are successively set equal to zero,
' impedance at terminals 1—1' with 2-2/ open
An
A22 „
- — — &oi
An-22
a = impedance at terminals 2-2' with 1-1' open
-~- = Zoi2 = ^021 ~ transfer impedance from either end with the opposite end open
Thus the network may be described by either of these sets of three parameters, or by
other sets of three parameters properly related to them.
* Foster, Geometrical Circuits of Electrical Networks, Trans. A.I.E.E., June 1932.
FOTJE-TEEMINAL NETWORKS
5-11
The driving point impedances and admittances are subject to the same restrictions
as any other two-terminal networks, if they are to correspond to physical networks. The
transfer functions, however, differ in several impor-
tant respects and require further consideration.
For the terminated network of Fig. 12 it can be
shown that
(*+£)•
(32o)
(326) FIG. 12. Terminated Four-terminal
Network
The response of the network evidently depends on the terminations Z\ and Zo, as well as
on the network parameters themselves. Thus the driving point impedances become
(33)
(34)
An •
And the transfer impedances ZT = Er/I\
ZT = - ^~ [A -f 2
A22
The form of the transfer impedance expression is seen to be the ratio of determinants
(since eq. [34] can be written ZT — — A/Ais if A is understood to be the network determi-
nant including the terminations Z\ and Z%), The general impedance coefficient is
Zab — LabP + Rab + Dab(l/p) as before. In terms of the frequency variable p — /<o,
therefore, the transfer impedance is the ratio of polynomials in p and can be written in
terms of its zeros and poles with a constant multiplier, just as in the case of driving point
impedances. Thus
Z A*(P ~ ^(P - OQ ' ' ' (P - O ,x
T
Bn(p -
- 62) - - - (p - bn)
Since ZT represents a transmission it is usually stated as a logarithm. And also, since
the most efficient possible transmission between two impedances Z\ and Zi is obtained if,
first, the reactances of Z\ and Z^. are annulled, and then a transformer of optimum ratio is
inserted between the two, this condition is used as a reference. Then the general transfer
impedance is _
ZT = 2VRiR&8 (36)
where
-- •" - (37)
(P - &i)(p- 62) • • • (p - W
and RI and RZ are the real parts of Z\ and Z%. The o's and 5's are the zeros and poles of ZT,
or the points of infinite gain or loss in terms of 9. It is evident from eq. (37) that two
transfer impedances having the same zeros and poles can differ only by a constant loss
or gam.
RESTRICTIONS FOR PHYSICAL REALIZABILITY. The restrictions which must
be met if ZT is to correspond to a physical network are as follows:
1. In terms of the frequency variable p both the zeros and the poles must be real or
must occur in conjugate complex pairs.
2. The real and imaginary components are respectively even and odd functions of fre-
quency.
3. The zeros must be located in the left half of the p plane; the poles may occur in any
part of the plane.
4. The real part of 0 — A 4* jB is positive at real frequencies; otherwise, the network
serves as a source of power.
On comparing these restrictions to those given for two-terminal impedances two im-
portant differences are noted. First, the poles of the transfer impedance are not restricted
to the left half-plane, and second, the real part of the transfer impedance may be negative.
The previous restriction that the real part of a driving point impedance be positive is
replaced by the new restriction that the real part of & must be positive.
5-12
ELECTEIC CIKCUITS, LINES, AND FIELDS
A structure which may be used to represent the general passive transfer function is
shown in Fig. 13. The arms of the symmetrical lattice are assumed to be inverse such
that Zy.Zy = R#. For this structure the ratio
where
Zx
Zx
(38)
(39a)
(396)
It can be shown that
FIG. 13. Network Having Any Prescribed Pas-
sive Transfer Function
to phase-shifting networks,
the combinations of factors
p + a
p - a
represents a physical impedance as long as 0 satisfies the re-
strictions listed above. In particular, Zx will
be physical as long as the transfer loss A is
greater than zero at real frequencies. Con-
sequently, in any case hi which the minimum
value of A is finite, the loss may be reduced
by a constant corresponding to this minimum
value. The reduced expression having zero
loss at a real frequency is called a minimum
loss or minimum attenuation function.
It is also possible to modify the transfer
phase B without affecting the loss by intro-
ducing, or eliminating, terms corresponding
Physical networks can be found (article 10) corresponding to
and
(p — a — jb} (p — a + jb)
(40)
Note that the poles in these expressions occur in the right half of the p plane, and that
the zeros and poles are the negatives of one another. The absolute value of these expres-
sions is evidently unity for all values of p, but the phase angle depends on p.
If the function ZT contains a single pole on the positive real axis,
ZT
F(P)
p - a p +
F(p) ip + a\
3 + a \p - a)
(41)
The transfer impedance ZT is thus the product of a new transfer impedance ZT' and a
phase-shifting term, and can be shown to correspond to a new network of transfer im-
pedance ZT' in tandem with a simple phase network. A similar treatment is possible for
a pair of complex poles in the right half-plane. The modified transfer impedance having
no poles in the right half-plane is termed a minimum phase function. No further reduction
can be made in the phase characteristic of such a function without at the same time
affecting the loss characteristic.
NETWORK THEOREMS. Several useful theorems can be stated for the general
linear network as follows:
The Compensation Theorem. If an impedance AZ is inserted in a branch of a network
the resulting current increment produced at any point in the network is equal to the cur-
rent that would be produced at that point by a compensating voltage — 7A.Z acting in
series with the modified branch, where / is the current in the original branch.
The Reciprocity Theorem. If an electromotive force E of zero internal impedance
applied between two terminals of a network produces a current I in some branch of the
network, then the same voltage E acting in series with the second branch will produce the
current I through the first pair of terminals shorted together. This follows from eqs. (30)
since the short-circuit transfer admittance is the same from either end of the network.
Thevenin's Theorem. With respect to any pair of terminals considered as output
terminals the network can be replaced by a branch having an impedance Z&, equal to
the driving point impedance at these terminals, in series with an electromotive force E,
equal to the open-circuit voltage across these terminals. An analogous theorem can be
expressed in terms of the short-circuit current entering the output node of the network.
FOUR-TERMINAL NETWORKS 5-13
These results follow from eq. (306) and the definitions of the open-circuit impedances and
short-circuit admittances. Thus, if EZ = — IzZz,
(42)
(43)
Za) ZQl(Z32 + Za)
The open-circuit voltage at terminals 2 — 2' is — I«Zz when £2 — » °° , whence
The short-circuit current at terminals 2 — 2' is — Ei Y8iz, whence
l2'
EQUIVALENT QUADRIPOLES. A useful concept in network analysis is that of
"equivalence." Two four-terminal networks, or quadripoles, are considered to be equiva-
lent when the fundamental relations describing the behavior of the networks with respect
to their input and output terminals are identical. Such equivalences can be expressed
in terms of the network determinant and its minors, the open-circuit impedances, the
short-circuit admittances, or any other set of three convenient and properly related
parameters.
IMAGE PARAMETERS. An important and useful set of parameters is based on
the idea that the terminations of the network be so related to the network itself that
the impedances looking in both directions from the input terminals, or in both directions
from the output terminals, are the same. Referring to Fig. 12 and eq. (33) this means
that Zi-i = Zi and £2-2' = Zz. The impedances Zi = Z/: and Z2 = Z/2 are called
image impedances and are functions of the network itself, since
and Z/a =
The third parameter necessary to characterize the network is called the image transfer
constant and is defined as
That is, 6 is one-half the logarithm of the ratio of the volt-amperes entering the network
to the volt-amperes leaving the network when it is terminated in its image impedances.
In terms of the network determinant
The value of these parameters lies in the fact that they offer approximations to the actual
network behavior and serve to relate the behavior of a network to that of a transmission
line.
T AND IT NETWORKS. The interrelation of several sets of network parameters is
shown for two fundamental types of four-terminal networks in Fig. 14. The branches of
the T and TT networks equivalent to the general network are given in terms of the network
determinant and its minors, the open- and short-circuit impedances, and the image
parameters. These branch impedances and admittances themselves constitute complete
sets of network parameters, even though they may not be physically realizable as two-
terminal networks at all frequencies.
The T and TT networks are important since they can be used to represent any quadripole
for purposes of analysis and computation. They may evidently be used to represent any
three-terminal network, or segment of a network, without loss of generality. The L-type
network is considered to be a degenerate case of the T or TT networks, and it is significant
in that only two independent parameters are required to specify its behavior.
LATTICE OR BRIDGE NETWORKS. A network of major importance is the sym-
metrical balanced lattice shown in Fig. 15. It can be shown that this network is the
most general of all symmetrical networks, and that any passive symmetrical four-terminal
network, or quadripole, can be represented by a physically realizable lattice. Further,
since the image impedance depends only on the product and the image transfer constant
only on the ratio of the branch impedances, it is possible to control the transmission and
impedance characteristics independently. See Section 6, article 23.
5-14 ELECTRIC CIRCUITS, LINES, AND FIELDS
tanh 6 =»
= ZA + Zc -
YF
Symmetrical: (An = A22t -Z"oi
— ZJB = Z7 tanh -
, = YE = YI tanh -
Yl
FIG. 14. T and ir Networks Equivalent to a General Dissymmetrical Network
2Z,
An - Aig
tanh 5/2
Zi — v'zxZy tanh - =- \ —
FIG. 15. Lattice Network Equivalent to Any Symmetrical Network and to T and Bridged-T Net-
works
POWER TRANSFER 5-15
The lattice equivalent to the symmetrical T and bridged T structures of Fig. 15 is seen
to be physical as long as the branch impedances of these structures are physical. The con-
verse is not necessarily true, since each of these networks requires that the arms of the
lattice contain a common impedance.
8. POWER TRANSFER
Transmission through a network is usually expressed as a logarithm with respect to a
suitable reference condition.
Transition Loss. The condition for maximum power transfer from a generator to a
load is indicated in Fig. 16. The series reactances — JS"i and — Xz are inserted to annul
the corresponding reactances of the generator and load impedances, and the ideal trans-
former of optimum ratio matches the resistance of the generator to that of the load.
This structure is termed an ideal transducer, and the loss in power which is eliminated when
it is inserted between a generator and a load is
called the transition loss or the transducer loss. In
decibels the
T>
Transition loss — 10 logio -~
Pz
= 20 logio | Zi + Z2 | - 10 logio 4R& (47)
where Pso = EP/^Ri is the reference power in the
load ( = available power) and P2 = ffRz/l Zi + Z2 12 FIG. 16. Ideal Transducer
is the actual power in the load.
Insertion Loss and Phase. When a network is inserted between a sending impedance Z\
and a receiving impedance Z^ a change occurs in the current (or voltage) in the load.
The ratio of the original load current 120 to the new load current /2 is denned as the insertion
loss factor or the insertion factor. In terms of the image parameters this becomes
•*20 -p
i; = <T
where ,
fa = -— — -1 = the sending end reflection factor
Z\ + Zi^
2VZzZi2
fa = — - = the receiving end reflection factor
fc — L_? 3— the reflection factor between Z\ and Z%
0 = the image transfer constant
S = ~ 7^ ^-TTTZ ^— ; T = the interaction factor
The reflection factors represent modifications in the load current caused by reflections
at the input and output junctions. The factor k, sometimes called the symmetry factor,
represents a reflection factor that was eliminated when the network was inserted. Each
of these factors involved only the ratio of two impedances, and each becomes unity when
the impedances are equal.
The interaction factor, S, is a second-order effect which takes account of a wave reflected
from the load back to the generator and then back to the load. It reduces to unity when
either termination matches the image impedance adjacent to it, or when the attenuation
of the network is high.
The insertion factor becomes equal to efl when one of the terminating impedances and the
image impedances are equal to one another.
The insertion loss (in decibels)
= 20 logio
- 2o|~ - logio i4r + logic r^-r + logio r^-r + logio r^T + IQ&O t £ 1 1 (49)
L I « I l^il i«2l 1^1 -I
5-16 ELECTRIC CIRCUITS; LINES, AND FIELDS
The first three terms, involving the reciprocals of the reflection factors, are called reflection
losses. The fourth term is called the interaction loss, and the last term represents the real
part of the image transfer constant in decibels,
The insertion phase shift is the phase angle of the current ratio given by eq. (48).
9. DISTORTION
When a voltage of complicated wave form is introduced into an electric circuit, a current
will flow whose wave form will depend on that of the voltage and on the transmission
characteristics of the circuit itself. It is frequently desired that the wave form of the cur-
rent through a particular circuit element shall be the same as the wave form of the original
voltage. If the complicated impressed voltage is regarded as a series of sine waves of
various frequencies the conditions under which the output current will be a faithful
reproduction of the input voltage may be stated as follows :
1. The response of the circuit must be the same for all frequency components present
in the impressed voltage.
2. The relative phase relations of the various frequency components must not be
altered.
3. The circuit must be linear.
FREQUENCY DISTORTION. When the first condition is not satisfied and the rela-
tive amplitudes of the various frequency components are altered, it is said that frequency
distortion occurs. This type of distortion occurs when the voltage-current characteristic,
that is the transfer impedance characteristic, is a function of frequency. Where the whole
transmission apparatus (including any mechanical and acoustic portions) is considered,
there are two methods by which the effect may be minimized. Each component part of
the system may be so designed as to have its response independent of frequency, or some
elements of the system may be designed to correct for the distortion introduced elsewhere.
Both methods of design have been widely and successfully used, the choice for a particular
case being decided usually by economic considerations.
DELAY DISTORTION. The requirement that the relative phases of the various
components be unaltered is equivalent to the requirement that the time of transmission
of the system be independent of frequency. To see this, consider a voltage consisting of
a group of sine waves applied to the system. In complex notation
« - 23 JBdW+to (50)
fcl
The received current will be
*i
where Zk ~ \ Zk \ f&k is the transfer impedance of the circuit at each frequency &k/2ir.
It is evident that frequency distortion will be present if | Zk \ is a function of frequency
within the band of frequencies considered. If it be assumed that [ Zk \ = R and that
Pk = «$i =fc nir, where R and t\ are constants and n = 0, 1, 2, • • • , then
, to
* - ± 4 S &#*»*<*-** +dk] (52)
R *i
The effect of the transfer impedance is to delay each component by an amount ti but to
leave the relative phases unaltered. The change in sign which occurs when n is odd is
usually not important.
If, on the other hand, (3% — &kti + <r(u>) ± mr, where <r(&>) is not a linear function of
frequency, the wave form of the received current will be different from that of the impressed
voltage even though the relative amplitudes of the current components are correct. (For
a discussion of non-linear distortion see Non-linear Electric Circuits.)
10. CORRECTIVE NETWORKS
A corrective network, or equalizer, is a network inserted between a generator and a
load such that the current in the load will vary with frequency in a predetermined manner.
A loss, or attenuation, equalizer is one which is used to control the amplitude of the received
current as a function of frequency without regard to phase relations. A phase equalizer
CORRECTIVE NETWORKS
5-17
is one which ideally introduces no loss but does introduce phase shift as a function of
frequency.
In most cases it is sufficient to equalize only for changes in loss. If, however, both
loss and phase equalization are required, it is usual first to equalize for loss, and then to
correct the phase of the system plus the loss equalizers. The incidental loss characteristic
introduced by the phase equalizer (because of power dissipated in the ideally reactive
elements) is usually ignored. If necessary, this distortion is corrected by an additional
loss equalizer designed as an integral part of the phase equalizer.
LOSS-PHASE RELATION. It is generally true that no unique relation can exist
between the loss and phase characteristics of a four-terminal network. However, as noted
in article 7, there is a unique relation between a given loss characteristic and the minimum
phase shift that can be associated with it. This relation is of value in the design of correc-
tive networks and feedback amplifiers, where it is necessary to control both loss and phase
over wide frequency ranges.
For the minimum phase condition it is possible to derive a number of relations between
loss and phase. One of the simplest is
/ /3 du = - (A^ - AQ) (53)
»/ — » 2
where w = log CO/COQ, /o ( = coo/2-n-) being an arbitrary reference frequency, 0 is the phase
shift in radians, and AQ and Aw are the losses in nepers at zero and infinite frequency
respectively. This states that the area under the phase curve, when plotted on a
logarithmic scale, depends only on the difference in the losses at zero and infinite frequency.
A second and possibly more useful relation is given by
"°° dA 1 u 1
— log coth —1 du
— co au 2
(54)
where &Q represents the phase shift in radians at any arbitrary frequency /o ( = coo/2?r) and
u = log W/WQ. This result states that the phase shift at any frequency is proportional to
the derivative of the loss, on a
logarithmic frequency scale, at
all frequencies. It involves an
integration over the entire fre-
quency spectrum. The function
log coth | u |/2 is in the nature
of a weighting function and is
shown in Fig. 17. Its value is
much larger near the point co — coo
and tends to emphasize the effect
of the loss characteristic in the
immediate vicinity.
As an illustration of the utility
of eq. (54) let it be supposed that
A — ku, which describes a loss
curve of constant slope on a log-
arithmic scale of 20k db per
decade (Qk db per octave). The
associated phase shift is readily
found to be k-rr/2 radians. As a
J.O
10.
FIG. 17. Weighting Function in Loss-phase Formula
second example consider the discontinuous loss characteristic of Fig. IS. Here the loss is
assumed to be zero below a specified frequency /o ( = coo/2?r) , and has a constant slope of
6k db per octave above coo/27r. The associated phase shift shown in Fig. 18 is symmetrical
about the frequency /o, at which point fi = k-jr/4, and approaches the value kir/2 radians
as frequency increases. At low frequencies the phase shift is substantially linear and is
giyen by jS = 2&co/(7rcoo).
Since the phase characteristic corresponding to the sum of two loss characteristics is
the sum of the two phase characteristics corresponding to the separate loss characteristics,
it is possible to add a number of such simple characteristics together to simulate more
complicated loss characteristics and to evaluate the corresponding phase shift. An ex-
ample is furnished by Fig. 19, which shows a phase curve derived as the algebraic sum of
three simple solutions of the type shown in Fig. 18. By proceeding in similar fashion it is
possible to derive the phase shift corresponding to almost any loss characteristic without
actually performing the integration indicated in eq. (54). In this connection it should be
observed that, if both the loss and the corresponding phase can be specified at all fre-
5-18
ELECTRIC CIRCUITS, LINES, AND FIELDS
quencies, the problem of designing an equalizer having the inverse characteristics is imme-
diately reduced to that of finding a two-terminal impedance for which both resistance and
reactance are known. See article 7.
llOfci
Mfofcj
90k
70k
60k
sofc
40k
30k
20k
10k
-lOfc
'&.
1.0
22k
20k
I0k%
8k
2k
iOD.
FIG. 18. Semi-infinite Slope of -.Attenuation (4) and Corresponding Phase Shift (J?)
25k
20k
0
30k
m 10fc
!
I °
— lOfc
— 20k
100.
FIG. 19. Phase Curve Corresponding to Sum of Three Semi-infinite Attenuation Slopes
LOSS EQUALIZERS. The networks commonly used as loss, or attenuation, equalizers
=are shown in Fig. 20, which also gives the expressions for the insertion loss factor.
The networks shown are divided into classes based on their transmission and impedance
properties. The simple series and shunt networks designated la and Ib are most useful
CORRECTIVE NETWORKS
for simple problems. Their transmission characteristics depend, of course, on
nations.
5-19
The L-type networks desig-
nated as Ha and lib have the
same form for the insertion
loss factor as la and IZ>. They
have the additional property,
however, that the input imped-
ance is equal to a constant, -&0,
when they are terminated in RQ
on the output. Consequently,
several sections can be operated
in tandem without interaction,
and the insertion loss of each
section is independent of the
generator impedance.
The symmetrical T, x, bridged
T, and lattice networks shown
as Ilia, Ill&JIIc.and Hid have
insertion loss factors identical to
the preceding network. How-
ever, they have constant-resist-
ance image impedances. As a
consequence the insertion loss
factor has the form shown if
either the generator or load im-
pedance has the value RQ. Net-
work IIIc is the most generally
used because it requires fewer
elements than any of the others.
The network shown as IV is
a general constant-resistance
lattice structure of which IIIo*
is a special case. This is the
most general form of constant-
resistance network, since any
transmission characteristic
which can be realized can be
obtained with a structure of
this form. See article 7. It is
possible, therefore, to base the
design of all equalizers on this
structure, even though the net-
work may be built in one of the
other forms when such a conver-
sion leads to a physical network.
The insertion loss factor, ee, is
somewhat more complicated for
this network than for the others
listed.
In terms of the admittance of
the Z\ arm
(55a)
Configuration
+ 1
where YI = (^ + jBi.
If 61 is assumed to be con-
stant with frequency, the net-
work can be shown to behave
as either a minimum phase or a
non-nodnimum phase network as
both termi-
tnsertlon Loss Factor
•7,
Ro~Ri+R2
Ro*
RiR2
116
UTa
IIT5
--£• ZiZ^-Ro
=!+7
xv
FIG. 20. Equalizer Configurations and Insertion Loss Factors
5-20 ELECTRIC CIRCUITS; LINES, AND FIELDS
the product RoGi is greater or less than unity. An explicit expression for YiRo in terms
of 6 is evidently
RoYl " " C0th
A fairly general approach to equalizer design based on the constant-resistance lattice
structure has been discussed by 0. J. Zobel.* This method provides a systematic means
of determining a network to satisfy a given loss requirement.
Referring to eq. (55a) it is a relatively simple matter to evaluate <? corresponding to a
given admittance 7i. A more difficult problem is to determine 7i for a given set of
values for a, since in a typical problem the corresponding value of (3 is usually unknown.
The design procedure is briefly as follows. The insertion power ratio is written as a
function of frequency thus
= ao + am2 + 02CQ4 + • • •
bo + 6iw* + 52cu4 + - - • Wj
where the a's and b's are real constants. A set of linear equations in the a's and 6's is
determined by assigning values to 620! at specific frequencies. As many frequencies are
selected as the number of coefficients to be determined. The solution of this set of equa-
tions gives the values of the a's and 6's required, and the function e2* is determined. The
roots of the numerator and denominator of e2a are then found in terms of p2 = — co2.
Since the function must lead to a physical network in order that it be useful the condi-
tions must be satisfied that
1. eza be greater than 1.0 for all values of co.
2. The roots of the numerator may not occur at real frequencies — otherwise e2a would
have a point of infinite gain.
3. The roots may be real or conjugate complex pairs.
4. The roots of the denominator may be anywhere in the p2 plane, but those that fall
on the negative real axis must be of even multiplicity — otherwise e2a will jump from
4- oo to — oo in this region, and so violate restriction 1.
If these conditions are satisfied the design proceeds. If not, a change is required;
either the assumed form for tza or the matching points must be altered.
To specify the network the function ee is formed. The roots of e2* are known in terms
of p2, and the corresponding roots in terms of p are readily available, since they occur
in + and — pairs.
The roots of the numerator used to form e0 must be in the left-half of the p plane. The
roots of the denominator are not necessarily so restricted. However, if this restriction is
applied to them also, the solution for ed will lead to a minimum phase network.
Utilizing the resulting function e6 the lattice arm impedance Zi, or admittance FI, is
determined from eq. (556). The network which exhibits this impedance may be found
in a variety of ways. A general method for solving this problem has been described by
O. Brune.f
As an example of the design process consider that the function to be matched is
#* = 1 + w6
In terms of p2 — — o>2 this becomes
<?« = 1 - p6
The roots of e20£ are given by p2 = 1.0 and p2 = — 0.5 =t ^0.866. In terms of p the roots
having negative real parts are then p = — 1 and p = — 0.5 db j'0.866, and
€0 = (p -f 0.5 - y0.866)(p + 0.5 + y0.866)(p + 1)
= p3 + 2P2 + 2p 4- 1
whence
'
Expanding this as a continued fraction by removing alternately poles and zeros the result
is obtained that
The corresponding impedance of the series arm of the lattice is shown in Fig. 21 for unit
impedance and unit frequency.
*O. J. Zobel, Distortion Correction in Electrical Circuits with Constant Resistance Networks,
.S.T.J., Vol. VII, July 1928, pp. 438-534.
t Journal of Mathematics and Physics, M.I.T., VoL X, October 1931.
COKEECTIVE NETWORKS 5-21
For many problems the analytic method of design which has been discussed is cumber-
some and unsuitable. For example, if it be required to equalize a measured characteristic
with only a fair degree of accuracy, the effort required to obtain a precise solution is not
justified. In such cases a knowledge of the behavior of the simpler forms of two-terminal
impedances can be usefully applied. The ability to visualize the frequency characteristic
of a configuration of coils, condensers, and resistances is an essential part of the designer's
equipment.
Probably the most useful configuration for design purposes, since it is one of the simplest,
is that shown as IIIc in Fig. 20, in which the impedance Z\
consists of a reactance shunted by a resistance. For this %
network o—
- 1 + . v (57)
where GI is a constant. Maximum loss occurs when BI — 0, .-, 01 T ,. . , T
while minimum loss (a = 0) occurs when BI -» «>. The FlG' 21> Lg££ ^
design problem is reduced, once a selection has been made of
the maximum loss required, to finding a suitable reactance, or susceptance, to match the
loss curve over the required interval. From eq. (57) it is evident that
(59)
Bf)
whence
For known values of e2" corresponding values of BI can be found. A relatively slight
effort is required to determine the required susceptance. The conditions for physical
readability are here merely that the zeros and poles occur at real frequencies, that they
alternate, and that the reactance function behave as a simple coil or condenser at zero or
infinite frequency.
In applying this process to build up complicated loss frequency characteristics as the
sum of several equalizer sections the skill of the designer is evidenced by his ability to
select easily realizable characteristics for the component sections.
PHASE EQUALIZERS. The constant-resistance lattice network IV of Fig. 20 be-
becomes an "all-pass" network when the impedances Zi and Zz are specified as pure
reactances. Then
Ro- JX1
e2« =1.0 and tan f = =fc ^
2 ti
There are two basic networks of this type, which are shown in Fig. 22. For the first of
these (Type I)
9 _ RQ + Lp _ p + BO/L
~ R0-Lp - p -
The zero of this expression is real and negative, and the pole is real and positive. In the
p plane they occur symmetrically on either side of the origin. The phase curve correspond-
ing to this network is shown in Fig. 22; the critical frequency co0
In the more complicated network shown as Type II in Fig. 22
where
and
<*\ i r
PI - -» = T MC^ [-
5-22
ELECTRIC CIRCUITS, LINES, AND FIELDS
When 4:R(?C/L :g 1.0 the zeros and poles are real. The zeros occur in the left half of the
p plane, and the poles are in the right half-plane. The network is, therefore, equivalent
to two of the simple types in tandem.
When 4:R<?C/L > 1.0 the zeros and poles are complex. Again the zeros are in the left
half-plane and are conjugate complex numbers. The poles are again in the right half-
plane and are symmetrically disposed about the origin. As would be expected a wide
variety of phase characteristics can be obtained. Some typical curves are shown in Fig. 22
plotted against w/co0. Note that, when 4RQZC/L = 1.0, the phase shift is exactly twice
that of Type I.
Increasing the complexity of the reactances in the lattice arms merely introduces addi-
tional zeros and poles in the expression for ee. If the network is to continue to be an all-
pass network, the zeros and poles must occur in pairs having characteristics similar to
FIG. 22. Typical Phase Characteristics of All-pass Networks
those noted above. Consequently, it is possible to break down a more extensive set of
zeros and poles into groups, each group corresponding to a physical network of either
Type I or Type II. A number of these simpler networks in tandem will provide charac-
teristics exactly similar to those of the more complicated lattice.
BIBLIOGRAPHY
Bode, H. WM Network Analysis and Feedback Amplifier Design. D. Van Nostrand (1945).
Gardner and Barnes, Transients in Linear Systems, Vol. I.
Bmne, O., Journal of Mathematics and Physics, M.I.T., Vol. X, October 1931, pp. 191-235.
Darlington, S., Journal of Mathematics and Physics, M.I.T., Vol. XVIII, No. 4, September 1939, pp.
257-353.
Foster, R. M.f A Reactance Theorem, B.S.T.J., April 1924, pp. 259-267.
Foster, R. M., Geometrical Circuits of Electrical Networks, Trans. A.I.E.E., June 1932.
Guillemin, E. A., Communication Networks, Vol. II.
Zobel, O. J., Distortion Correction in Electrical Circuits, B.S.T.J., Vol. VII, July 1928, pp. 438-534.
RECURRENT NETWORKS
By P. H. Richardson
Early work on transmission networks was from the viewpoint of wave propagation in
uniform media. Later work introduced the methods of particle dynamics, and networks
were treated as vibrating systems. In treating the problem of recurrent networks, that
is, the problem of a number of similar networks in tandem, the terminology of the earlier
method is most useful. A3 might be expected, the problem is readily handled in terms of
equivalent line parameters such as the image parameters previously defined.*
* Solutions of the general problem in terms of botk image and iterative parameters are given by
E. A. Guillemin, Communication Networks, Vol. II, pp. 163-175. In the case of symmetrical networks
the two sets of parameters are identical.
SYMMETRICAL NETWORKS
5-23
11. SYMMETRICAL NETWORKS
CURRENT AND VOLTAGE RELATIONS. Consider the tandem combination of two
symmetrical networks shown in Fig. 1. The image impedance is assumed to be the same
for both structures, while the transfer constants QI and 02 are different. To find the voltage
FIG. 1. Tandem Combination of Symmetrical Networks
at the junction x-x' replace the generator and network to the left of the junction by
an equivalent Thevenin. generator. Then the open circuit voltage at x-x'
EZi
The voltages Ex and EI are evidently given by
#.._
,_ „. and
E
The impedances Zi', Zs', and J£x* are given by the relations
Zi'-.
(i)
(2)
(So)
(36)
(3c)
where pi ~ * , - and p2 = * . ,, are the reflection coefficients at junctions 1-1'
Zti + Zil 42 -\- Z,I
and 2-2' respectively.
Substituting in eq. (2) It can be demonstrated that
where
jfia; £ri
J' " 2? " Zi
and
(4)
(5)
(6)
Note that AI and 5i depend only on the sum of the two transfer constants and the reflec-
tion coefficient at the output junction.
INCIDENT AND REFLECTED WAVES. The term JM^-ft is called the incident
component of the voltage, and EiBi€6i is called the reflected component of the voltage. Like-
wise the terms (Ei/Zi)Aie~8i and —(Ei/Zi)B^ are called the incident and reflected
components respectively of the current at the junction x-xf. Note that if Zz — Zi,
that is, if the impedances are matched at the output, there is no reflected component since
BI = 0. Also, if 61 + 0$ has a large positive real part, BI becomes very small, and again
the reflected component vanishes. The voltage ratio and the current ratio are both equal
to €~dl, when the reflected "wave" is zero.
IMPEDANCE RELATIONS. The pair of networks having like image impedances
behave as regards the input and output meshes as though they together constituted one
network of image impedance Zi and transfer constant 0i + #2- When the output im-
pedance matches Zi, pa = 0 and the impedances Z\ and Zx" are both equal to Zi. Note
also, if the real part of 0i + 62 is large, the input-impedance again is equal to Zi.
5-24
ELECTRIC CIRCUITS, LINES, AND FIELDS
A relation which is frequently useful in design problems can be obtained from eq. (3).
The reflection coefficient at the input terminals
p./
pl
l' - Zl
Thus the reflection coefficient at the input terminals, pi/, is simply related to the reflection
coefficient at the output terminals. If 0i + Q% is a pure imaginary, then | p\' \ = | p2 |
Also, if a is the real part of 0i -f- 62, then | pi' | — 1 P2 I
*-2os
12. UNIFORM LINES— NETWORKS WITH DISTRIBUTED CONSTANTS
When the physical dimensions of a network are comparable to the wavelength of the
electric current flowing in it, account must be taken of the fact that the series resistance
and inductance of each wire, and the shunt capacitance and leakage between wires, are
"distributed." Such networks are usually termed transmission lines (see also Section 14
in volume on Electric Power), but in the case of very high-frequency currents (5 meters
or less) a network contained within an ordinary room may have to be similarly treated.
The usual transmission line in communication circuits consists of two similar parallel
wires, or a single wire enclosed in a conducting cylindrical sheath. At every point on the
line, some current flows from one wire to the other, or to the sheath, owing to capacitance
and leakage conductance resulting from the imperfect dielectric between them. In conse-
quence of this, the current in each conductor varies along the line. This is illustrated in
Pig. 2, which shows an elementary section of a balanced line, or of a completely unbalanced
%Zdx
%Zdx
o — VV^- nfflT^--nSW^-AM — oC Ao — -W — ''TO^-o— 'TKftP — W> — o
>Y dx^p
%z dx
%z dx
-dx-
E
-dx-
where Z-r+jLco and Y=£7+j"Cw
FIG. 2. Elementary Section of a Transmission Line
line equivalent to the coaxial type of construction. The current entering at A is not the
same as that leaving at (7, owing to the capacitance and conductance shunted between
B and E. Hence the total drop due to the total resistance of the line is not this resistance
multiplied by the current at any point on the line. Simple impedance equations cannot
be written; simple differential equations can be given (for this solution see Section 14 in
volume on Electric Power) , and these offer one method of attack.
An alternative method is based on the assumption that such a uniform transmission
line may be considered to be composed of an infinite number of symmetrical networks,
each of which corresponds to an infinitesimal length of line. If r is the resistance and L
the inductance per unit length (for two wires, sometimes called a loop-mile when the
unit of length is a mile) , and g the conductance and C the capacitance between the wires,
or from the central conductor to the sheath, per unit of length, then, in a section of length
dx, there will be a resistance r dx, an inductance Z/ dx, conductance g dx, and capacitance
C dx. As dx approaches zero the sections become smaller, and a line of these sections
approaches a line with uniformly distributed constants.
VOLTAGE AND CURRENT RELATIONS. Let Z = T + jLu = | Z \ /J^ be the series
impedance per unit length, and let Y = g + yCco = | Y \ /6y
A A be the shunt admittance per unit length of line. Then
for the T network equivalent to an infinitesimal length
of line (see Fig. 3) for which 6 = d&
PIG. 3. T Network Equivalent to
Smooth Line
Zc = T~ ~
dd
-
Y dx
(8a)
(86)
UNIFORM LINES 5-25
Thus
7 - \
Zl -
This impedance is frequently called the characteristic impedance of the uniform line; the
terms image impedance and iterative impedance which are also used are somewhat more
clearly denned. They are, of course, identical to one another for the symmetrical lint*.
From eqs. (8) it follows that d6 = VZT dx, whence
(10)
where x represents the distance to a point on the line from the sending end. The quantity
7 is called the propagation constant of the line and is evaluated per unit length of line. For
a given length of line the total propagation constant is seen to be identical to the image
transfer constant of the equivalent symmetrical network. 7 is a complex number and can
be expressed as y = a + jjS, where « and j3 are real. Expanding eq. (10) and separating
reals and imaginaries
+ (rg - LCco3)] -(Ha)
L2a>2)(g2 + C2^) - (rg -
The parameters a. and $ are called the attenuation constant and phase shift constant, re-
spectively, of the line. Note that they are both functions of frequency.
The relations given by eqs. (9) and (10) indicate the similarity between the behavior of
networks having lumped constants and the behavior of uniform lines. At some point a
distance x from the sending end of a line of length I the voltage Ex and current Ix are
given by eqs. (4), (5), and (6) of article 1, where 0i = yx and 82 — *y(l — x). Similarly
the input impedance of the line is given by eq. (3a) .
INCIDENT AND REFLECTED WAVES. The instantaneous voltage at any point
on the wire is
and
ix = Real part
ex = Real part [E^^A^-v* +
= | Si | [I Ai | €-«* cos M - |8a: + 84) + | Bi | e** cos (tat + 0x + 5*)3 (12)
|~ J^ 4** (4ie— >* -
1 €~^ cos (w* - jSa; + 6^1 - *) - I Bi | «aa; cos M 4- ]5a; + SB - *)] (13)
where J.i = | Ai \ /5A, BI = | BI ] /5g, Zj = | Z/ | /^ and EI is real.
Each of these expressions is composed of two components, the incident "wav&" which
decreases in magnitude as x increases, and the reflected "wave" which increases as x increases.
These components are called "waves" because they appear to travel along the wire with
a velocity v = co/£. The distance between two consecutive points on the line at which
cos (u>t — fix + 5 A) and its derivative have the same algebraic values for a fixed value of t
is called a wavelength (X), so that /3A = 2-Tr. The time elapsing during a complete cycle
of values is called the period (T) , so that T — I//. In terms of these values the velocity
of phase propagation of the waves is T? = <u/£ == \/T.
STANDING WAVES. The combination of the incident and reflected waves, adding
sometimes in and sometimes out of phase, causes variation in the value of the voltage
and current with position along the line. The expression for the amplitude of the voltage is
I Ex | = | Ei | V| Ai |26-2o* + | jgj |2e2oz + 2| AI ]| BI | COS (203 + 65 - 8 A) (14)
and for the current,
| Ix I = -~ V| -di |2€-2o^ -j- | j5x |2€2o:a:_ 2J AI || BI | cos (2j3x + SB — 5j.) (15)
each of which will have maximum and minimum values along the line whenever | BI \ ?£ 0,
since cos (2px + SB — 8 A) changes more rapidly than e2ax. When attenuation is negligible
and I Ai \ = \ Bi |
\EX\ = | EI |[ Ai 1 V2[l + cos (2$x + SB — 8 A)] (16)
5-26 ELECTRIC CIRCUITS, LINES, AND FIELDS
From this it is evident that there are positions where \ Ex\ — 2\ E\ \\ A\ \ called voltage
loops, and others where | Ex \ — 0 called voltage nodes. Similarly there are current loops
and nodes, the current nodes corresponding to voltage loops, and vice versa.
It should be noted that the condition that | AI \ = | BI \ requires that p^~^1 = ±1.0.
Thus true standing waves occur only when the line is a multiple of a quarter wavelength
and when pz — =1=1.0, that is, when Zz is either zero or infinite.
INPUT IMPEDANCE. The input impedance of a uniform line terminated in an im-
pedance #2 at a distance x from the sending end is given by
" z. 1
l~ '
where pz — ^ - — • li Z% = Zi, then p2 = 0 and Zi = Zi* The variation of Zi with
£2 -h Zi
frequency is a smooth wave which approaches the value VL/C as / increases.
When Z% j£ Zi the Zt- vs. / curve has maxima and minima which can be approximately
located. If it be assumed that Zi and Z% are pure resistances, which together with a are
independent of frequency, then the locus of Zi in the Zi plane is a circle of radius
(18a)
with its center at
/I A. n^~4ax\ 1 ^
If p2 is positive (Z% > Zi), Zi will have its maximum or minimum value when e~^x is +1
or — 1. This requires that 2/3x = 2mr, or (2n — I)TT, where n is any integer. Since
j3 = CO/B the frequency at which the maximum or minimum occurs is given by
run (C)"" — 1^"
/max. — r~ or /min. —
If / = /i when n — n\ and / = /2 when n = n\ + 1, then
2(/2 - /i)
But since /2 — /i is the frequency interval between two successive maxima, or two suc-
cessive minima, the distance x to the point on the line at which there is an impedance
discontinuity can be determined approximately. It should be noted that the expressions
for the frequencies at which maxima and minima occur will be interchanged if p2 is negative
(Z* <Zfi.
DISTORTIONLESS LINES. In communication systems many frequency components
are usually present, and it is desirable to have uniform attenuation with frequency. This
condition exists on a line if r/L = g/C, in which case
a = Vrg and
both of which are independent of frequency. Similarly, j3 — ccVZC, which is the condition
for linear phase shift and no delay distortion. In this case also
ft VLC
which states that all waves are propagated with the same velocity.
TRANSIENTS IN NETWORKS
By Harold A. Wheeler
13. TRANSIENT DISTURBANCES
PROPERTIES OF TRANSIENTS. A transient disturbance, in its simplest concept,
is one that occurs in a time interval separated from other disturbances. In general, a
transient may be superimposed on other transients or continuous waves, according to the
superposition theorem, while otherwise retaining its own characteristics. A single tran-
TRANSIENT DISTURBANCES
5-27
ents, -§A
K&). I
itch- I'
sient cannot be a periodic wave in the strict sense, although it may be a damped oscillation
of a definite period. A borderline case is the "periodic transient," which is a periodic non-
overlapping series of transients; each transient retains the properties of a transient while
the series has the properties of a periodic wave.
Any periodic wave can be analyzed into a "Fourier series" which is a sum of sinusoidal
components of frequencies hi harmonic relation. The corresponding representation of a
transient disturbance is possible by the "Fourier integral," which does not give a number
of distinct components but rather the distribution of energy over the frequency spectrum.
The Fourier series and the Fourier integral are analogous to the line spectrum and the
band spectrum in light waves.
In general, an exact representation by a Fourier series requires an infinite number of
components extending over the entire frequency spectrum, but a practical approximation
requires only a limited number of components within a limited bandwidth. The same
is true with respect to the limited bandwidth required for the practical reproduction of a
transient. It is essential to consider the degree of approximation required or attained in
any particular case, and to realize that both the duration of the transient and the frequency
bandwidth are theoretically unlimited although practically limited by the sensitivity of
the system.
Refer to Section 9, Pulse Techniques, for much information on transients as exemplified
by pulses, with emphasis on their application in practical systems.
TYPES OF TRANSIENTS. It is convenient to define transient disturbances of several
idealized types. An actual transient may be classified by its similarity to one of these
types, or as the response of
a certain network to one of I
these types. !
The unit step is one of
the elementary transients,
shown in Fig. l(a) and , .
It may be caused by switch- | ' + —•
ing or keying a current or
voltage of unit amplitude.
The form of Fig. 1 (a) is also
called the "Heaviside unit
function, ' ' with a j ump from
zero to one. The form (6)
has a jump from — 1/2 to -M/2; it is preferred for some analytical purposes because it has
zero d-c component. Campbell and Foster (references 7 and 8) designate the unit step as
jS_i, called the singularity function of —1 order.
The unit impulse, shown in Fig. l(c), is unique among transients in that it has a uniform
frequency spectrum. It is defined as the derivative or slope of the unit step; therefore it
has unit area as the product of very large amplitude and very small duration. It is also
called by Hansen the "delta function" (reference 38). Campbell and Foster (references
7 and 8) designate the unit impulse as So, called the singularity function of zero order.
In practice, the step is easier to generate because of its limited amplitude, and the
transient response thereto has limited amplitude. The impulse may be approximated
with limited amplitude if its duration is reduced until its frequency spectrum is substan-
tially uniform over a frequency bandwidth sufficient for any particular tests. Most net-
works have some integrating action, so their response, even to an ideal impulse, would
have limited amplitude.
Some oscillatory transients are illustrated in Fig. 2. In general, there are reversals of
polarity, which may or may not be periodic in time. The transient response of a practical
network is usually oscilla-
tory in some degree. Fig-
ure 2(o) shows a damped
oscillation which is a com-
mon occurrence; Fig. 2(6)
shows a pulse-modulated
wave including several
f ^ _. cycles of a carrier wave,
W W (C) while (c) shows a carrier
wave with a step in its
modulation envelope. A
(a)
(o)s,
FIG. 1. Unit Step and Unit Impulse
FIG. 2. Oscillatory Transients
carrier wave cannot be conceived as modulated by the ideal impulse, because the duration
is insufficient to retain the identity of the carrier frequency.
Practical steps have finite slope, and practical pulses have finite duration and amplitude.
5-28
ELECTRIC CIRCUITS, LINES, AND FIELDS
For test purposes, however, both can be made to approach the ideal as closely as required,
so the transient response of a network to the ideal types can be tested.
A pulse to be used for modulating a carrier wave is sometimes denoted a "d-c'* pulse
to distinguish it from the modulated carrier of pulse envelope. The essential difference
is in the frequency spectrum, the former having most of its energy concentrated in a band
including zero frequency, and the latter in a band including the relatively high carrier
frequency. The direct and carrier pulses are distinct concepts if their respective frequency
bands are separate.
Amplitude modulation of a carrier wave generates symmetrical sidebands, and pulse
modulation follows this rule. The carrier and both sidebands are needed for exact repro-
duction of the modulation. A small modulation superimposed on a continuous carrier,
as illustrated in Fig. 2(c), can be approximately reproduced in a system responsive to one
sideband and one-half the relative carrier amplitude, as employed in television (references
5, 11, 12, 16-19, 21, 24, 25, and Section 20).
FREQUENCY SPECTRUM. Figure 3 shows the frequency spectrum of several kinds
of disturbances. The pure sine wave has a single frequency component (a). A periodic
wave in general, such as a repeating short pulse, has a series of frequency components of
relative amplitude indicated
by an envelope of the lines
(6) . A transient has a con-
tinuous frequency spectrum
(c) . If the transient has the
same shape as a single cycle
of the periodic wave, the con-
tinuous spectrum (c) has the
same frequency distribution
as the envelope of lines (6) .
a fundamental frequency, denoted /i in Fig. 3, and all
~l
Frequency
fa
FIG. 3. The Frequency Spectrum of Periodic Waves and Aperiodic
Disturbances
Periodic disturbances have . ,
components are harmonically related on integral multiples of this frequency. A transient
lacks a fundamental frequency but, like the periodic wave, still requires frequency com-
ponents over a certain band width for its reproduction with sufficient approximation. In
Fig. 3(c), a nominal cutoff frequency fe may be defined in such a way as to include most
of the energy of the frequency spectrum. For pulse operation, the nominal cutoff fre-
quency on the frequency spectrum of amplitude may be denned as the boundary of a
rectangle (drawn as shown in dotted lines) having the same area as the amplitude spectrum
(reference 11).
In the line spectrum of a periodic wave, each component has a definite amplitude which
may be expressed in terms of current or voltage (or analogous linear quantities) . In the
band spectrum of a transient, however, the amplitude is expressed per unit of frequency
bandwidth, in units such as the volt per cycle per second or volt-second. This concept
is elusive, but the shape of the spectrum indicates clearly the relative importance of the
various frequency components.
As an alternative, the frequency spectrum may be presented in terms of relative energy
instead of amplitude. It is then expressed in terms of energy per unit of frequency band-
width, in units such as the joule per cycle per second or joule-second. The area under the
curve is the total energy of the transient.
The frequency spectrum of Fig. 3 shows the relative response of a receiver of very narrow
and constant bandwidth as it is tuned over the frequency range. Spectrum analyzers are
operated on this principle, some of which show the
spectrum directly on an oscilloscope (Section 9).
SPEED OF INFORMATION. In communica-
tion of any kind, the available frequency band-
width is limited, and this may restrict the speed of
transmission (references 2, 4-6, 9-11, and Section
9) . This is one of the principal limitations in pic-
ture transmission.
As a simple example, Fig. 4 shows the code pulses
for the word "as." The pulse pattern (a) contains
dots and dashes in the form of short and long
pulses. It is necessary to distinguish the presence
or absence of a pulse at intervals of one pulse width.
A A A
^ -- \ --- /\7\T\ --
* - ' * — *' *
(&)
FIG. 4. Speed of Information by Pulses
Increasing the speed or decreasing the frequency bandwidth up to a certain limit has the
effect of rounding the pulses (6) but not filling in the space between pulses. This much
distortion is permissible and economical in practice.
The rounded pulses in Fig. 4(6) have a frequency spectrum similar to that in Fig. (3c)
BEHAVIOR OF NETWORKS
5-29
if the dots have a width 2tc related to the nominal cutoff frequency fe as follows (reference
11):
2tc " W (1)
4/C
This means that the shortest pulse or space has a duration of 1/2 cycle at the nominal
cutoff frequency. The speed of information is proportional to the number of pulses in a
given interval which is proportional to the frequency bandwidth.
A completely modulated carrier requires twice the bandwidth because double-sideband
operation is essential, A partially modulated carrier, with single-sideband operation as in
television, requires only slightly more bandwidth than the modulating pulses but also
requires more power to surmount background noise and interference.
14. BEHAVIOR OF NETWORKS
DIFFERENTIATION AND INTEGRATION. A linear network operates only on the
amplitude and phase of a sine wave, retaining the wave form. Though the same is true
of each component of a transient, the operation on all components may greatly change
its shape. The simplest distorting operations of networks are differentiation and inte-
gration.
The two basic differentiating networks are shown in Fig. 5. In each case, the input
and output are denoted by subscripts 1 and 2. In (a) and (fe), the series capacitor C and
the shunt inductor L are so connected that each gives an output proportional to the
time derivative of the input;
Fig. 5 (a) -r-^ C = I2; (6) -37 L = E$
(2)
The instantaneous voltage and current are here denoted E and /.
C , L
(a)
FIG. 5. Basic Differentiating Net-
works
(a)
FIG. 6.
Basic Integrating Net-
works
If instead the amplitudes of the frequency components are denoted E and I, the corre-
sponding relations for any particular frequency may be written:
Fig. 5 (a) EijuC = J2; (&) lii<»L = E2 (3)
Here j is the quadrature factor V— 1 and &> = 2ir/ is the radian frequency. The two sets
of equations are alike in form except that d/dt is replaced by j'w; this explains why jw is
sometimes called a differential operator. It includes the inseparable two essentials of
differentiation, namely, an amplitude ratio directly proportional to frequency and a lead-
ing phase shift of one quadrant.
An example of differentiation is the conversion of a unit step to a unit impulse. The
former has frequency components of amplitude inversely proportional to frequency,
while differentiation changes it to the impulse having frequency components of uniform.
amplitude.
The two basic integrating networks are shown in Fig. 6. In (a) and (6), the series
inductor L and the shunt capacitor C are so connected that each gives an output propor-
tional to the time integral of the input :
~
(4)
Changing the significance of voltage and current, E and I, from the instantaneous values
above to the amplitudes of the frequency components:
Fig.6(a) *-
< JBt
(5)
Since Cdt is replaced by !//«, the latter is sometimes called an integral operator. It
5-30
ELECTRIC CIRCUITS, LINES, AND FIELDS
includes the inseparable two essentials of integration, namely, an amplitude ratio inversely
proportional to frequency and a lagging phase shift of one quadrant. An example of
integration is the conversion of a unit impulse to a unit step.
The basic networks of Figs. 5 and 6 rely on simple admittance or impedance coupling,
so the input and output are voltage and current in one order or the other. Approximate
differentiation and integration can be obtained by voltage-ratio or current-ratio coupling,
the former being shown in Figs. 7 and 8. Each of these networks includes a resistor R in
FIG. 7. Voltage-ratio Differenti-
ating Networks
FIG. 8.
Voltage-ratio Integrating
Networks
addition to a reactor C or L. The required approximation to the ideal operation in
each case places, certain requirements on the time constant of the network, which is
L/R or OR.
Figure 9 shows the meaning of the time constant in a charging or discharging operation
(a) or (6) . In each case the transient has an exponential variation with time, and the time
constant t\ is the length of time required to approach completion of the operation. Quan-
titatively, it is the time to go to (1 - 1/e) or 0.63 of completion (e = 2.72, the base of
natural logarithms) .
Though the concept of charging and discharging is commonly associated with energy
storage by the voltage on a capacitor, it is equally applicable to energy storage by the
current in an inductor.
A charging operation shown in Fig. 9 (a) is exemplified by a voltage step applied to an
integrating network of Fig. 8. The integrating operation continues only for a duration
less than the time constant, so the time constant must be longer than the required
period of approximate integration. This is a general rule for such integrating net-
works.
A discharging operation shown in Fig. 9(6) is exemplified by a voltage step applied to a
differentiating network of Fig. 7. The differentiating operation is prolonged for a duration
exceeding the time constant, so the time constant must be shorter than the permissible
duration. This is a general rule for
such differentiating networks.
Meeting these conditions in Figs. 7
and 8 is promoted by a large value of
series resistance or a small value of
shunt resistance, so the voltage ratio
is small for the frequency components
of major importance.
G. 9.
(a) (6)
Tune Constants of Charging and Discharging
Figure 10 is a chart of the charging and discharging operations obtained from the net-
works of Figs. 7 and 8 in response to steps and impulses.
OSCILLATIONS. If differentiation and integration are mixed in a network by com-
bining CLR, the result is resonance. The transient response to a step or impulse may then
be a damped oscillation. Figure 11 shows examples of voltage-ratio resonant networks
and the response of each to certain input transients. A resonant network is one having
maximum response at the frequency of resonance; an antiresonant network is one having
minimum response at that frequency. Either one exhibits damped oscillations after a
transient disturbance. The time constant of damping in the series-resonant circuit is
2L/R, while that in the parallel-resonant circuit (with parallel R) is 2CR.
REPEATING NETWORKS. There are many kinds of networks which respond to a
step or impulse with interesting and significant output transients. One of the simplest
is the integrating network of Fig. 8(6) repeated in successive stages of a vacuum-tube
amplifier (No. 524.2 in references 7 and 8, also reference 38) . Figure 12 shows the response
of n such networks to an impulse. The integrating action, denoted by the time constant
tit both delays and widens the pulse by virtue of the energy storage in each capacitor and
its subsequent discharge (by repeater action) into the next capacitor. The delay of the
pulse exceeds the widening, so this system is a crude delay network. The pulse peak is
delayed by (n — l)£i. For large values of n it is widened to V2T \/n — 1 ti, and it
approaches the symmetrical shape of a probability curve.
BEHAVIOR OF NETWORKS 5-31
Input (Ej) Network Output Eg)
(a) D-c on
(5) D-c off
Impulse
D-c on
Integrating
Integrating
Integrating
Differentiating
Charging
Dls'cheirging
Discharging
Discharging
(e) D-c off Differentiating Discharging
FIG. 10. Transient Response of Simple Networks
Input (Ei)
Output (
A-c off
(C) In
A-c on
or
Resonant
Resonant
Anti- resonant
Rising
FaHlng
ftA A/\ ^ ^ .>
ri-rjTnsrw^rr
Falling
Falling
T
A-c off Anti-resonant Falling
FIG. 11. Transient Response of Oscillatory Networks
5-32
ELECTRIC CIRCUITS, LINES, AND FIELDS
The response of a resonant circuit to an impulse, as exemplified in Fig. 1 1 (c) for a single
network, may be extended to repeating networks. The envelope of the resulting transient
oscillation then assumes the form of Fig. 12.
FIG. 12. The Delay and Widening of a Pulse by Repeating Integrating Networks
BANDWIDTH. The integrating action of a shunt capacitor limits the speed of in-
formation by restricting the frequency bandwidth. This is a major factor in a wide-band
amplifier for such uses as television and radar, because each interstage coupling from one
tube to the next has inherent shunt capacitance. Figure 13 shows a resistance-coupled
amplifier stage subject to inherent shunt capacitance C across the coupling resistor R.
The frequency variation of the response of such an amplifier is shown in Fig. 14, in
which /i is the frequency at which the reactance of the capacitor (l/[27r/C]) is equal to the
shunt resistance (R). Figure 14(a) shows the amplitude variation for several conditions,
starting with (1) simply R and C. The bandwidth is increased (2) by adding inductance L
to build up the impedance by a tendency to resonance. A more complicated network,
2
(a)
///!
f/A
FIG. 13. Amplifier with Shunt Ca- FIG. 14. The Limitation of Bandwidth by Shunt Capacitance
pacitance Limiting the Bandwidth
termed the "dead-end filter" (reference 15), can be used to extend the bandwidth as far
as curve (3) but no further. The maximum bandwidth over which a uniform amplitude
ratio can be obtained is theoretically
In practice, about half this bandwidth is obtained in simple circuits with a sufficient
approximation to uniformity.
If many stages of wide-band amplification are needed, the phase distortion shown in
Fig. 14(6) may be a limiting factor more severe than amplitude distortion. The ideal
phase variation is a linear proportionality to the frequency. Condition (1), with simply
R and C, yields a convex phase curvature, but in this case the amplitude distortion is
more severe. (See Fig. 12, which applies to this case.) Condition (2), with L added,
yields a concave phape curvature which happens to be more detrimental than the residual
amplitude distortion. There are cases (notably in radar pulse receivers) where a com-
promise between (1) and (2) may be optimum (reference 38). The extreme condition (3)
yields abrupt changes in amplitude and phase at cutoff, which cause transient damped
oscillations.
GENERAL PRINCIPLES 5-33
AMPLITUDE AND PHASE DISTORTION. The transient response of linear networks
is related uniquely with their steady-state characteristics, so a knowledge of the latter
makes it possible to estimate the transient response. This is the province of the Fourier
integral and other concepts such as "paired echoes" for evaluating distortion (references
14 and 20). Examples of amplitude and phase distortion are shown in Fig. 14 for the
simple case of Fig. 13 described above.
Amplitude distortion may be simply the limitation of the bandwidth or may also include
irregularities within the bandwidth. It is generally expressed in terms of attenuation,
since this is a logarithmic quantity which can simply be added for cumulative stages
(p. 1-37).
Phase distortion is any departure from linear proportionality between the lagging phase
angle and the frequency. It is expressed in angular measure, which is additive for cumu-
lative stages. The absolute unit of angle is the radian, which is l/2ir circle or 57.3°, The
radian is quantitatively comparable with the napier, so 6.6° is comparable with 1 db.
The inherent properties of passive linear networks determine certain relations between
attenuation and phase angle (references 36 and 41) . For any pattern of variation of the
attenuation over the entire frequency range, there is a corresponding pattern of -mim'trm-m
phase angle obtainable in networks. Those networks which provide selective attenuation
with minimum phase angle are termed " minimum-phase" networks and others "excess-
phase" networks. Minimum-phase networks include self-impedance couplings, simple
ladder networks, and any other network whose response can be expressed as a product of
physically realizable self-impedance factors. Excess-phase networks include transmission
lines, all-pass phase-correcting networks (lattice or bridged-tee), and networks with
negative mutual inductance.
Phase-correcting networks are theoretically possible free of attenuation, but not atten-
uation-correcting networks free of phase distortion. Therefore it is customary, in the
design of a practical network, first to obtain the required attenuation, and then if necessary
to add phase-correcting networks for obtaining linear phase. Usually the phase correction
need be effective only over the band width of nearly maximum response. Phase correction
(free of attenuation) always increases the phase angle, never the reverse.
Amplitude distortion, free of phase distortion, cannot destroy the symmetry of a sym-
metrical input pulse. Therefore any asymmetrical distortion is a symptom of departure
from phase linearity.
A sharp cutoff at the edge of the useful bandwidth causes a damped oscillation or "over-
shoot" in the transient response to an impulse or, in less degree, to a step. If this result
is not permissible, a gradual cutoff is required, as shown in Fig. 3(c) (reference 11).
15. GENERAL PRINCIPLES
THE FOURIER INTEGRAL. In the study and design of networks to handle transient
disturbances, the most powerful concept is the Fourier integral. It is an extension of the
more familiar Fourier series, which is restricted to periodic waves but still serves as an
introduction to the integral. Each is essentially a relationship between a disturbance
over a period of time and its frequency components; or, conversely, a set of components
can be synthesized into the form of disturbance.
The following presentation of the Fourier series is in a form well adapted for extension
to the integral and useful for direct application.
A wave form (of voltage or current, for example) is denoted T(t} and is completed in
the time interval between — ti/2 and -Hi/2. The same wave form is repeated hi successive
intervals of the same period fr, as a periodic wave. This wave can be expressed as a sum
of sine-wave components of harmonic frequencies and the proper phase:
00
T(t) = S Fn exp (j2*nfiQ (7)
n= — oo
The fundamental frequency is /i = l/fc. Each harmonic component has a frequency nfi
which is an integral multiple of the fundamental frequency. Its amplitude is Fn, which
is generally complex to include the phase angle. Obviously the dimensional units of T(f)
and Fn are the same.
The sine-wave nature of each component is indicated by the unit vector rotating at a
frequency nfi :
exp (fiirnfit) = cis (2irnfit} = cos (2™/i«) -f / sin (2-irnfit) (8)
Since T(f) is real, it is apparent that the imaginary parts of each component in the summa-
tion must cancel out. This cancellation occurs between the amplitudes Fn of the com-
5-34 ELECTEIC CIRCUITS, LINES, AND FIELDS
= r
j -K
ponents of equal positive and negative values of n. The zero-frequency (direct) com-
ponent (n =* 0) always has a real amplitude FQ.
The (complex) amplitude of each component is formulated as
"h/2
T(t] exp (-ftirnfit] dt (9)
'-'1/2
This integral selects and evaluates each harmonic of frequency nfi. A tabular or graphical
or formal integration can be used to compute Fn, which in general will be complex.
The extension of the series to the integral requires two more concepts. First, since a
transient is presumed to occur only once, the period ti is made very large and the corre-
sponding fundamental frequency /i very small. Secondly, the harmonic amplitude Fn
is changed to the frequency spectrum F(f) which represents the "amplitude-frequency
density" or "amplitude per unit of frequency" in the vicinity of the frequency/ (instead
of nfi). The density does not have the same dimensional units as TOO but rather the
same units multiplied by "time." For example, if T(£) is in volts, F(f) is in volts per cycle
per second, or volt-seconds.
With these steps, there follows the Fourier integral for expressing the wave form of a
transient in terms of its frequency spectrum F(f) :
T(t) = C F(f) exp (/27T/0 df (10)
J — 00
The other form expresses the frequency spectrum in terms of the transient:
F(f) = r™ T(t] exp (-/27T/0 dt (11)
J — 00
Following Campbell and Foster (references 7 and 8), the above forms are symmetrical
in that F(f) and T(t} are interchangeable merely by reversing the sign of/. This is accom-
plished by integrating from — =o to + °° , and expressing in terms of the variables / (instead
of to = 2x/) and t, which are mutually reciprocal. These forms include j2ir under the
exponential function, which is logical since J%TT is the natural logarithm of a unit vector
rotated by one cycle, and exp (/27r) symbolizes that vector.
In electrical networks, the interchangeability of F(f) and T(t} has reality only if F is
real, since T is real. This is true only in idealized networks, which may be instructive
examples. In such cases, both F and T are symmetrical in form.
The direct significance of F(f) and T(t) is simple. It is based on the unique fact that
an impulse has a uniform amplitude density over the spectrum. If a unit impulse is
applied to a network which modifies its frequency spectrum to the form F(f), the output
is a transient of the form T(t).
If a transient TI of any shape is applied to any network, the output transient T can
be expressed and often evaluated simply by the following procedure: (1) compute FI, the
spectrum of the input transient TI\ (2) formulate F2, the frequency response of the net-
work; (3) note that the frequency spectrum of the output transient is F — FiF%', (4) from
the knowledge of F, use the Fourier integral to express the out-
put transient T. If the input is a unit step instead of a unit
impulse, Fi = l//2?r/.
Closely related methods of transient analysis and synthesis are
the Laplace transformation and the Heaviside operational calculus.
The Fourier integral is a restricted case of the Laplace transform,
but actually the one which is most simply adapted to the study
of transients in electrical networks. The operational calculus is
merely a process for deriving, explaining, and applying some of
the ideas inherent in the Fourier integral. The present state of
the literature places the Fourier integral in a position to be of the
greatest aid in solving network problems.
THE SUPERPOSITION THEOREM. Any transient can be
regarded as built up of a number of steps or pulses, a large num-
ber for smooth wave forms. This is the basis of the superposition
theorem. A simple example, and probably the first to be dis-
covered, is shown in Fig. 15. A square pulse (a) of any width is
the resultant of two superimposed steps (6) , the first one positive
_, and the second negative. The transient response of a network to
IG* Superpositfon *ke sQuare pulse is obtained by first evaluating its response to each
step (c) and superimposing these transients (d).
The FiFz procedure described above has an alternative in the superposition theorem
of the operational calculus. This theorem is encompassed in a single Fourier integral (No.
202 in references 7 and 8). As above, TI is the input transient (whose frequency spectrum
GENERAL PRINCIPLES
5-35
is F{) and F2 is the response of the network; T% is the transient which would be obtained
from the network in response to a unit impulse. The output transient is then expressed
in terms of T\ and Tz as follows:
T(t) = f
J —
exp
df
- £') dtf « f °° Ti(t - t'}
J — 00
dtf
(12)
(13)
The symbol tf denotes the variable of integration, as distinct from i, the time variable in
the transient.
THE ENERGY INTEGRAL. One of the most useful corollaries of the Fourier integral
is the "energy integral":
r \p\*df- r T*dt (u)
J — 00 */- CO
It states that the energy of the transient is proportional to the area under the energy-
distribution curve over the frequency range, this curve being plotted in terms of 1 F ]2.
This concept has the widest use for the evaluation of the power associated with random
noise, which behaves as a great number of impulses occurring at random. It is noted
that the total energy is determined by the amplitude (squared) independent of phase.
IDEALIZED FILTERS. Idealized examples of niters and transients are instructive
as to the basic limitations. The most common such example is shown in Fig. 16 (references
(6)
(o)
FIG. 16. An Idealized Filter and Its Transient Response
9 and 10). A network (a) has uniform response (with zero phase angle) up to a cutoff
frequency /c, and no response above this frequency. If an impulse is applied to this
network, the output transient (&) is symmetrical and is accompanied by transient oscilla-
tions at the cutoff frequency. If this response is approximated in a real network, the
phase slope is rather great and delays the main pulse so much that the earliest perceptible
oscillations (preceding the pulse) occur at a time later than the applied impulse. Inci-
dentally, this requires an "excess-phase" network as defined above.
In the transient of Fig. 16(&), the nominal pulse duration may be denned as 2tc, deter-
mined by the dotted rectangle of equal net area. If a step (instead of an impulse) is
applied to the same network, the output (c) has a slope of the same nominal duration
(called the "slope time" or "time of rise'* or "build-up time").
The ideal filter of Fig. 16 (a) has a perfectly sharp cutoff, which causes transient oscilla-
tions in the output (6) and (c). The opposite extreme is a response having gradual cutoff
of the form of a probability curve, somewhat similar to Fig. 3(c) (reference 11). In re-
5-36 ELECTRIC CIRCUITS, LINES, AND FIELDS
sponse to an impulse, such a filter yields a rounded symmetrical pulse of the same shape,
free of overshoot and transient oscillations. This performance is approximated by a
large number of networks like Fig. 8, with output transients shown in Fig. 12. This case
has been found ideal in radar receivers, to assure the prompt damping of one echo pulse
in readiness for another.
BELAY. A lagging phase angle is characteristic of filters passing a limited band width
(low-pass and band-pass), and also of transmission lines. The result is a delay of the
signal, and perhaps also a distortion of its wave form.
The delay is defined in different ways, as a function of frequency. If /3 is the lagging
phase angle (in radians) at a frequency o> (in radians per second) , the " intercept delay"
or "phase delay" (in seconds) is merely /3/co. It signifies the delay of each sine-wave
component along the time axis. If the delay is the same for all components, it is free of
distortion. This result requires *' linear phase," that is, a phase angle directly proportional
to the frequency.
The more general concept is the "envelope delay," defined as the "phase slope"
dfi/du. This definition is free of the ambiguity of multiples of 2?r in determining the phase
angle. It derives its name from its significance as the delay of the envelope of a transient
oscillation of many cycles, as distinguished from the delay of the individual cycles. The
delay of the cycles is inconsequential if the transient is to be rectified, in which event the
envelope delay uniquely determines the effect of the phase angle on the output of the
rectifier.
These two definitions of delay correspond with those of the wave velocity in a trans-
mission line or other wave medium. The intercept delay or phase delay determines the
"phase velocity" or "steady-state velocity," with its ambiguities. The envelope delay
uniquely determines the "group velocity," -which, from one point to another, cannot
exceed the speed of light.
BIBLIOGRAPHY
1. C. P. Stemmetz, Transient Electric Phenomena and Oscillations, third ed. McGraw-Hill (1920).
(Many original concepts, mainly superseded by later methods of presentation.)
2. R. V. L. Hartley, Relations of Carrier and Sidebands in Radio Transmission, Proc. I.R.E., Vol. 11,
34-56 (February 1923). (Double or single sideband, with or without carrier.)
3. L. A. Hazeltine, Electrical Engineering. The Macmillan Co. (1924). Chapter 6, "Transient
Currents and Electric Waves," pp. 210-254. (The transient response in simple circuits and lines.)
4. H. Nyquist, Certain Factors Affecting Telegraph Speed, B.S.T.J., Vol. 3, 324-352 (April 1924).
(The limitation imposed by the frequency band width and the choice of a code.)
5. H. Nyquist, Certain Topics in Telegraph Transmission Theory, Trans. A.I.E.E,, Vol. 47, 617-644
(April 1928), (The relation between speed and frequency bandwidth; the case of single sideband
with half-amplitude carrier.)
6. R. V. L. Hartley, Transmission of Information, B,S.T.J., Vol. 7, 535-563 (July 1928). (The
amount of information proportional to the product of the frequency bandwidth and the time.)
7. G. A. Campbell, Practical Application of the Fourier Integral, B.S.T.J., Vol. 7, 639-707 (October
1928). (Purely mathematical introduction; table of paired coefficients.)
8. G. A. Campbell and R. M, Foster, Fourier Integrals for Practical Applications, Bell Tel. Sys. Tech.
PubL, Monograph B-584, September 1931. (Purely mathematical introduction; the most
extensive tables of paired coefficients.)
9. A. T. Starr, Transients in Networks, Electric Circuits and Wave Filters, Sir Isaac Pitman & Sons,
Ltd., Chapter 12, pp. 332-353, 1934. (Introduction to the concept of idealized networks and
their transient response.)
10. E. A. Guillemin, Communication Networks, Vol. II. John Wiley (1935). Chapter 11, "The
Transient Behavior of Filters," pp. 461-507.
11. H. A. Wheeler and A. V. Loughren, The Fine Structure of Television Images, Proc. I.R.E., Vol. 26,
540-575 (May 1938). (The band-width limitation, especially the effect of sharp cutoff or gradual
cutoff; a simple introduction to the Fourier integral in the absence of phase distortion; bibli-
ography.)
12. J. E. Smith, B. Trevor, and P. S. Carter, Selective Sideband vs. Double Sideband Transmission of
Telegraph and Facsimile Signals, R.C.A. Rev., Vol. 3, 213-238 (October 1938).
13. A. V. Bedford and G. L. Fredendall, Transient Response of Multistage Video-frequency Amplifiers,
Proc. I.R.E., Vol. 27, 277-284 (April 1939).
14. H. A. Wheeler, The Interpretation of Amplitude and Phase Distortion in Terms of Paired Echoes,
Proc,. I.R.E., Vol. 27, 359-385 (June 1939),
15. H. A. Wheeler, Wide-band Amplifiers for Television, Proc. I.R.E., Vol. 27, 429-438 (July 1939).
(Fundamental limitations imposed by shunt capacitance; idealized networks including dead-end
niters.)
16. R. TJrtel, Observations Regarding Television Transmission by Single Sideband, Telefunken Haus-
mitteilungen, No. 81, pp. 80-83 (July 1939). (The envelope distortion in the transmission of
single sideband and half-amplitude carrier through a filter of idealized characteristics.)
17. Leon S. Nergaard, A Theoretical Analysis of Single-sideband Operation of Television Transmitters,
Proc. I.R.E., Vol. 27, 666-677 (October 1939).
18. S. Goldman, Television Detail and Selective-sideband Transmission, Proc. I.R.E., Vol. 27, 725-732
(November 1939). (The envelope distortion in the transmission of single sideband and half-
amplitude carrier through a filter of idealized characteristics.)
19. H. Nyquist and K. W. Pfleger, Effect of the Quadrature Component in Single-Sideband Trans-
mission, B.S.T.J., Vol. 19, 63-73 (January 1940). (The envelope distortion in the transmission
of a single sideband and half-amplitude carrier through a filter of idealized characteristics^
NON-LINEAR ELECTRIC CIRCUITS 5-37
20. Von F. Strecker, The Influence of Small Phase Distortion on the Reproduction of Television
Signals, E.N.T., Vol. 17, 51-56 (March 1940); The Effect of Amplitude and Phase Distortion,
93-107 (May 1940). (Paired echoes.)
21. R. D. Kell and G. L. Fredendall, Selective Sideband Transmission in Television, R.C.A. Rev., Vol. 4,
425-440 (April 1940) . (Response of single-sideband receiver to a unit step of modulation.)
22. M. I. T. Engineering Staff, Electric Circuits. John Wiley (1940). (A comprehensive treatment
of networks with emphasis on their transient response.)
23. H. E. Kallmann, Transversal Filters, Proc. I.R.E., Vol. 28, 302-310 (July 1940). (The synthesis,
by a pattern of echoes, of the signal which would be produced by an idealized filter free of phase
distortion.)
24. H. E. Kallmann and R. E. Spencer, Transient Response of Single-sideband Systems, Proc. I.R.E.,
Vol. 28, 557-561 (December 1940). (The envelope distortion in the transmission of single side-
band and half -amplitude carrier through a filter of idealized characteristics.)
25. C. P. Singer, A Mathematical Appendix to Transient Response of Single-sideband Systems,
Proc. I.R.E., Vol. 28, 561-563 (December 1940).
26. H. S. Carslaw and J. C. Jaeger, Operational Methods in Applied Mathematics. Oxford University
Press (1941). (The Laplace transformation.)
27. H. A. Wheeler, The Solution of Unsymmetrical-sideband Problems with the Aid of the Zero-
frequency Carrier, Proc. I.R.E., Vol. 29, 446-458 (August 1941).
28. H. A. Wheeler, Common-channel Interference between Two Frequency-modulated Signals, Proc.
I.R.E., Vol. 30, 34-50 (January 1942). (The response to frequency modulation, by an analysis
which is general for any wave form of modulation, either transient or periodic.)
29. J. B. Russell, Heaviside's Direct Operational Calculus, Elec. Eng., Vol. 61, 84-88 (February 1942).
(A brief introduction.)
30. R. V. L. Hartley, A More Symmetrical Fourier Analysis Applied to Transmission Problems, Proc.
I.R.E., Vol. 30, 144-150 (March 1942).
31. W. L. Sullivan, Fourier Integrals, Elec. Eng., Vol. 61, 248-256 (May 1942). (An excellent intro-
duction and bibliography.)
32. H. Salinger, Transients in Frequency Modulation, Proc. I.R.E., Vol. 30, 378-383 (August 1942.)
33. A. V. Bedford and G. L. Fredendall, Analysis, Synthesis, and Evaluation of the Transient Response
of Television Apparatus, Proc. I.R.E., Vol. 30, 440-457 (October 1942).
34. M. F. Gardner and J. L. Barnes, Transients in Linear Systems, Vol. 1, "Lumped-constant Systems."
John Wiley (1942). (The most intensive treatment of the subject, based on the Laplace trans-
formation, with emphasis on electromechanical analogues. A complete bibliography.)
35. J. G. Brainerd, Ultra-High-Frequency Techniques. D. Van Nostrand (1942). Chapter 1, "Linear
Circuit Analysis," pp. 1-47. (Transient response to steps and pulses.)
36. F. E. Terman, Relation between Attenuation and Phase Shift in Four-terminal Networks, Proc.
I.R.E., Vol. 31, 233-240 (May 1943).
37. Harold Pender and S. R. Warren, Electric Circuits and Fields. McGraw-Hill (1943). Chapter 4,
"Introduction to Transient Phenomena in Electric Circuits," pp. 108-133.
38. W. W. Hansen, Transient Response of Wide-band Amplifiers, Proc. of National Electronics Confer-
ence, Vol. 1, 544-554 (1945); also Electronic Industries, Vol. Ill, No. 11, 80-82, 218, 220
(November 1944). (A definition of bandwidth for transients, and its application to amplifiers
of one to 100 stages.)
39. R. V. Churchill, Modern Operational Mathematics in Engineering. McGraw-Hill (1944).
40. W. W. Hansen, On Maximum Gain-bandwidth Product in Amplifiers, J. Applied Phys., Vol. 16,
528-534 (September 1945).
41. H. W. Bode, Network Analysis and Feedback Amplifier Design. _ D. Van Nostrand (1945). (A com-
prehensive treatment with emphasis on stability and bandwidth.)
42. H. E. Kallmann, R. E. Spencer, and C. P. Singer, Transient Response, Proc. I.R.E., Vol. 33,
169-195 (March 1945).
43. M. Levy, The Impulse Response of Electrical Networks, Elec. Com., Vol. 22, No. 1, 40-55 (1944).
(Idealized networks.)
44. G. W. Carter, The Simple Calculation of Electrical Transients. The Macmillan Co. (1945). (A
short mathematical course based on operational methods, with well-selected tables and bibli-
ography.)
45. Ernest Frank, Pulsed Linear Networks. McGraw-Hill (1945). (An introductory course limited
to the direct application of differential equations.)
46. D. G. Tucker, Transient Response of Filters, Wireless Engineer, Vol. XXIII, No. 269, pp. 36-42
(February 1946); VoL XXIII, No. 270, 84-90 (March 1946).
Note: Reference 31 is recommended as a good introduction to the more advanced concepts, and a
good bibliography to that date. References 29 and 31, with three related papers, have been reprinted
by A.I.E.E. under the title Advanced Methods of Mathematical Analysis (1942).
NON-LINEAR ELECTRIC CIRCUITS
By Knox McHwain
In solving the fundamental electric circuit equation
the assumption is often made that r, L, and C are constants. Circuits in which these
conditions exist are called "linear circuits" and have been treated above. If any one or
more of these circuit parameters vary with the current through it or the voltage across it,
the solution of eq. (1) hi general takes the form of an infinite series^ so that the current
wave form is not a replica of the voltage wave form. Such circuits are called "non-
linear circuits."
5-38 ELECTRIC CIRCUITS, LINES, AND FIELDS
NON-LINEAR DISTORTION. When it is desired that the wave form of the current
through a particular circuit element be the same as the wave form of the original voltage,
and when the response of the element is not directly proportional to the driving force
(non-linear circuit), the element is said to introduce non-linear distortion. When the
input voltage is a simple sine wave, the output current will contain components of double
and higher multiples of the impressed frequency, the amplitudes being determined by
the series solution mentioned above.
Non-linear distortion is most serious in sound reproduction since the spurious sound
harmonics are readily noted by the ear and produce a very unpleasant sensation for the
fastidious listener. If the rms value of the introduced harmonics is kept below 5 per cent
of the rms value of the fundamental, the non-linear distortion will not be objectionable
(sometimes even 10 per cent is allowed).
One important characteristic of this type of distortion is that, once introduced, it is
difficult if not impossible to correct for it, so that the component parts of the circuit must
be separately designed so as
to have linear voltage versus
current characteristics (except
Curjeni for modulators and detectors,
see Section 7) .
SOLUTION OF NON-
LINEAR CIRCUITS. The
change in inductance due to
the non-linear B-H curve of
iron, the varying resistance
of an electric arc or of the
thermionic vacuum tube, or
the varying capacitance of
the condenser microphone, all
introduce non-linear effects.
The simplest case is where the
resistance is some function of
Voltage voltage or current. Fre-
FIG. 1. Non-linear Current-voltage Characteristic quently this functional rela-
tionship is given as a curve of
current against voltage, as in Fig. 1. The first step is to fit an analytic expression to the
curve. Two methods have been widely used in communication practice:
(a) a power series of the form
i - A0 + Ai e + A2 e* -f A, e* + • - - (2)
(6) a trigonometric series
i - AQ + Ai sin (e + ft) + A* sin (2« + 0a) + • * • (3)
16. POWER SERIES SOLUTION
Such devices as thermionic vacuum tubes, electric arcs, some surface contacts (such as
copper oxide and lead), and certain crystalline structures have a current-voltage char-
acteristic similar to that shown in Fig. 1. Since the instantaneous value of the electric
resistance to an increment of current is Ae/Ai, the resistance varies with the applied volt-
age, or r — F(e).
The coefficients of the power series of eq. (2) may be evaluated as follows: If four
terms of the power series are of interest, choose four separated points on the current-
voltage curve and use the four sets of values of e and i in eq. (2) . Solve the four resulting
algebraic equations by any of the standard methods for AI, A%, etc. This method may
always be used no matter how irregular the curve and will always give correct results
for the points chosen; unless the curve is smooth it may give quite incorrect results for
intermediate points. The characteristic must be plotted including all resistance in the
circuit whether variable or invariable. It is extremely difficult to include the effect of
reactance in the circuit. The application of the method is thus limited, but it is useful
in certain special cases.
TAYLOR'S SERIES. If the equation of the current-voltage characteristic is known,
or if it can be found (it is frequently of the form i — Ke^ for at least portions of the curve,
in which case the constants can be evaluated by plotting on logarithmic cross-section
papfer), the solution by Taylor's series is useful in evaluating the coefficients of eq. (2).
TRIGONOMETRIC SERIES 5-39
The current at any point (e) in terms of the current at a particular point (EQ) can be
written.
*-
where the derivatives are all evaluated at the operating point (Eo). Care must be exercised
in using this formula that the voltage is confined to the region wherein the curve follows
the assumed law and within the limits of convergence of the series. A detailed treatment
of this method is given in article 20.
17. TRIGONOMETRIC SERIES
In some applications of devices such as vacuum tubes and gas-filled tubes, the devices
operate over a range large compared with the part of the characteristic shown in Fig. 1.
The application of a power series would usually, under such conditions, require an un-
reasonable number of terms in order to obtain even a fair approximation. On the other
hand, a trigonometric series with a properly chosen fundamental period permits the ex-
pansion of such a curve using only a few
terms for a fair approximation.
The trigonometric series is periodic by
nature and so does not represent the
\
-B
characteristic outside of the interval over A \ —
which the harmonic analysis was taken. \
When the curve is of the form dbc in Fig. 2 ot ^
and the voltage varies only over the in-
terval dbe, the curve can be arbitrarily FIG. 2. Construction for Use of Trigonometric Series
replaced by any other curve outside of
this interval. If the curve outside of this interval is replaced by a curve as shown by the
broken line in Fig. 2, such that the resulting curve is skew-symmetric about the point e and
symmetrical about the vertical axis through d, eq. (3) reduces to
i » j!0 4- AI sin e + AI sin 3e + • • • (5)
Because of the symmetrical properties of the resulting curve both the even harmonics
and the phase angles become zero. The choice of curve outside of the operating interval
so that the resulting curve has these properties of symmetry is always possible. The
convergence of the series is usually greatly increased by using this built-up curve (with
a fundamental period four times the distance from d to 0). However, other choices of the
curve outside of the working interval are even better in particular cases.
A fundamental period having been chosen and the curve having been completed through-
out this period, the coefficients of the harmonic sine functions can be determined by means
of one of the several available schemes for harmonic analysis (see article 24).
In most electrical engineering the e has the form of a constant voltage plus a series of
sine-wave voltages. When voltages of this form are substituted in eq. (5) and the suc-
cessive terms expanded by means of the trigonometric formulas for the sine and cosine of
the sum of two angles, the series consists of terms ^of the form cos (x sin d) and sin (a; sin d)
which can be expanded by the formulas of Jacobi
eo
cos (x sin d) = Jo(x) + 2 2 Ju(x) cos 2Rd
and
oo
sin (x sin d} = 2%J 25-1 (a?) sin (222 - l)d
where J»(a?) is a Bessel function of the first kind, of order n and modulus x. These functions
can be found in tables of Bessel functions. See p. 1-37.
By means of this expansion the amplitudes of the sinusoidal components of the current
flowing in any circuit can be calculated from the current-voltage characteristic of the
circuit provided that the circuit contains no reactive elements. No general analytic
method has yet been devised for the direct application of the trigonometric series in a
circuit containing reactive impedance analogous to that treated in article 20. However,
eq. (3) or (5) having been obtained, the differential coefficients of eq. (4) can be obtained
simply by differentiation.
This solution can be extended to the case of two or more independent variables as in
the application to the three-electrode vacuum tube with variable amplification factor and
5-40 ELECTRIC CIRCUITS, LINES, AND FIELDS
with independent voltages applied in both the grid and plate circuits. However, the work
is so voluminous that it is practicable only in very special cases,
18. INDUCTANCE VARIATION
When the variation of inductance is of importance the magnetization curve (locus of
the tips of the hysteresis loops) of the iron forming the (closed) magnetic circuit of the
reactor is required. This is usually similar in form to the curve in Fig. 1 with flux density
CB) as ordinates and magnetizing force (H) as abscissas. This curve must be replotted
in the form of i (the exciting current) as a function of <j> (the total flux). Then by
Taylor's formula
in which the derivatives are evaluated at the operating point. Define
"1.1
60 Jo LQ
where LO is the usual incremental inductance (apparent inductance to a changein current)
at the operating point. Then (see article 20)
and so forth. Also e = — d<f>/dt so that / e dt = — <j>. If increments are considered
<t> — 0o = 0a — — I ea dt
If ea = SEn cos (unt + 0n) as is usual (see article 21) , then
<t>a - -ea\ X -^ I
L j^J
where the symbol [X] indicates that the maximum value of each first-degree cosine term
of different frequency in the e immediately preceding is to be multiplied by the modulus
of the complex quantity within [X], and the phase angle of the complex (hi this case ir/2)
is to be added to the phase of the cosine, both modulus and phase being evaluated at the
frequency of the given cosine term (see article 20) .
Substituting these expressions in eq. (6)
Hence if the B-H curve were a straight line dL/d<f> = 0 and
^ En COS (tOnt + &n ~ 7T/2)
To obtain i in terms of the applied voltage E'a in the circuit containing the variable
inductance and a constant impedance z the same process employed in introducing imped-
ance load in the case of a varying resistance must be employed (see article 21)
There results
i = e'[ X PI] + «*[ X Qd + • • • (8)
where
1 _ 1
Ci = ; — r~y = —,
Z + JuLo T
which is to be so interpreted that
and
_ ] £.(c,)» f a
08 - ^+ ~
APPROXIMATE SERIES EXPANSION
which is to be so interpreted that
_ clmC2(n+g)z(n+g) + CinCa
5-41
,
19, CAPACITANCE VARIATION
When the variation of capacitance is of importance, as in such devices as the condenser
transmitter, eq, (1) may be rewritten as
and the characteristic of the device plotted as charge against voltage. The same methods
of solution used for resistance variation are then available (with the exception that the
operator z introduced in the detailed solution of article 21 must be replaced by /wz) .
20. APPROXIMATE SERIES EXPANSION FOR THE PLATE CURRENT
OF A TRIODE (ASSUMES |X CONSTANT)
Circuits containing thermionic vacuum tubes are chosen to exemplify the detailed
treatment of non-linear electric circuits because of the commanding importance of the
thermionic tube in communication
practice. This wide use has occurred
largely because the triode, tetrode,
etc., combine an amplification or con-
trol function with the non-linearity
of the current-voltage device; in
most tubes it is possible to employ
either or both functions by a simple
shift in electrode operating voltages
(see Section 4 for nomenclature and
characteristics) .
The triode is generally used in
practice with steady voltages applied
to both grid and plate, and in addi-
tion at least one varying voltage on
one of the control electrodes, and
frequently with one or more varying
voltages impressed in both the plate
and grid circuits; these instantaneous
currents (it, ic) and voltages (65, ec)
may be conveniently split up as
follows:
ib = It 4- ip
ic = Jo + v
70
60
50
40
30
15
10
9
8
7
5 4
3
2
1..5
1.0
f {
//
7
.Norrr
a Plate Voltage and
ri ament Current
f
Ec=0
-d
/I
/
1
1
1
1
I
/
1
/
/
1
f
/
1
1
\
~-c*
-1
4. t
1
Expon
ent«
1.86
t
/
^
/
/\
f
/
I 4 5 6 7 8 9 10 15 20 30 40 50 6C
•^~t-Ec-EquivaIent Total Grid Voltage irt Volts
e& — jE/6 -f- eP
where the capital letters (Ej,, Ec, J&,
7C) indicate steady values obtaining
before the application of any varying
voltages in the plate or grid circuits;
the lower-case letters with subscript
p or g indicate instantaneous values
of varying components. All these
voltages are specified as actual voltages between electrodes; if the external circuits contain
impedance these voltages will differ from the supply voltages.
The plate current of the usual triode is a function of ee, e&, and the amplification factor
FIG. 3. Mutual Characteristic of a Triode. Normal plate
voltage = 130 volts, n » 5.45.
5-42 ELECTRIC CIRCUITS, LINES, AND FIELDS
ju(= — deb'dec when ib is held constant) such that for at least portions of the operating
range
ib = K (- + ec Y (10)
where K and 77 are constants. The values may be found for any tube by plotting the plate
current of the tube against equivalent grid voltage ( -- f- ec J on logarithmic cross-section
paper as shown in Fig. 3. The value of 77 in most triodes usually lies between 1.5 and 2.5;
since it varies around 2.0 the triode is sometimes said to follow a square law. This may
be sufficiently accurate for rough calculations but is not satisfactory in an exact analysis.
Expanding by Taylor's series
where the subscript 0 after a bracket indicates that the derivatives are to be evaluated
for eb — EI, and ec — 28 e. Note that I& = F(JEt>, Be] and may be subtracted from each
side of eq. (11). Also define the static plate resistance as
(12a)
then
1 deb Jo
and
^2
TP
Making these substitutions, eq. (11) becomes
.- _ ^ '
+ ^eg) _ (ep + M%)2 drp~\ 2(ep + ^g)s /Bri\ V
rp 2rp* deb]o 3!rp» \deb]J
If, as is usual in amplifiers, ep — 0, then the factor }j./rp(= dib/dec) frequently appears in
this equation. It is designated gm and called the grid-plate transconductance (mutual
conductance). Expansions in terms of transconductance are particularly useful when n
is variable or when the plate resistance of the tube is so high that external resistances are
negligible (see article 22).
21. CHARACTERISTICS OF TRIODE WITH LOAD
When the triode is used with external impedance there are voltage drops in these
impedances so that the electrode voltages are the differences between the applied voltages
and these impedance drops. Since eq. (13) applies to the voltages between the electrodes,
account must be taken of the impedance drops.
RESISTANCE LOADS. When the external loads
are pure resistances the electrode currents and voltages
may be split up as follows (see Pig. 4) .
FIG. 4. Triode with Resistance Load e& = Eb + ep = E'b — rib + efp — rip
where ep is the sum of the externally impressed voltage and the load resistance drop in the
plate circuit, eg is similar, and r and re are the external resistances in the plate and grid
circuit. The voltages e'g and e'P are the driving voltages introduced in the grid and plate
circuits.
CHARACTERISTICS OF TRIOBE WITH LOAD 5-43
If the assumption is made that the plate-grid transconductance gn(^ dic/deb) is zero,
as is usual for small grid voltages, then the grid current (rg is the internal grid resistance) is
-L
*
and the varying voltage between grid and cathode is
eV* , eVr,rg drg
€*==^T^e + 2(rg + re^c+'-
The varying component of the plate current (let e = eg + efp/fj.) is
= W _ M2e% dri\ u?e*rp(2rp - r)
p rp + r 2l(rp + r)» ^ V 3l(r, + r)«
3!(rp
Usually the higher-order derivatives rapidly decrease in value, and, since in the higher-
order coefficients the power of (rp + r) in the denominator rises rapidly, all terms beyond
the third may be neglected for most practical applications of the tube.
IMPEDANCE LOADS. When impedances are connected in the external circuits of
the tube (instead of the resistances of Fig. 4) it is impossible to write the external imped-
ance drop in vector form until the plate circuit is specified. Use may be made of the
operational impedance z = r + L — -4- ^J^ "whkh is such that zi represents the im-
pedance drop regardless of the form of i. Of course it is impossible to evaluate zi until i is
known. The plate current may be written in terms of an operator denoting a delayed
multiplication, called the square cross bracket, as
ip = e[ X ci] + e2[Xcd + e»[Xcd+-.- (17)
where
-r-
in which z is to be separately evaluated for each component frequency of interest. Note
that z7 is the total impedance of the plate circuit at the particular frequency. Likewise
±*ii <s£ (19)
2 de6J0 z7
in which each of the c's is to be evaluated at the frequency of one of the original frequencies
beating together and z' is to be evaluated at the beat frequency. For instance, to find the
size of the current component of periodicity (COOT + ««) caused by the beating of two terms
of periodicity com and con, evaluate
T? TP r
EwlEnC2(m+n) = -
, , "
Z mZ nZ (m+n) <Jvb Jo
Similarly eg, which embraces terms caused by three of the originally impressed com-
ponents beating together (these are very important in calculating the amount of interfer-
ence introduced in a radio receiver by neighboring carriers), is
which is to be so interpreted that
n) &>"]
" 7^ L
Vet JO
Z <m-Kt+g)
5-44
ELECTRIC CIRCUITS, LINES, AND FIELDS
Table 1. Plate Currents of a Triode
1. No load and resistance load; n assumed constant.
ip = ae •+• c2e2 + cge3 + etc. (e = eg+—2
ci
0
e.
No load,
aq. (11)
V
-4; 21
3^1 Vlte6_U
^rpaVp-, 1
2 de&2Jo/
Resistance
load, «q.
(16)
j"
/i* rs arP-|
si^rM**1
r) f 3rpl V i
d'rp-, \
rp+r
2l(r, + r)»*J.
Vde&Jo/
PrP + r ^^
2. Impedance load; ^ assumed constant.
ip = e[Xci] + e2[Xc2] + e3[Xcs] + etc.
Cl
C2
C3
M M
rpdrp-i (Cl)2
ci(c2z) drp-i rp (ci)» /xdr,-. x 2 rp a^-i \
rp + z z'
eq. (18)
eq. (19)
eq. (20)
The expression e2[X c2] means that e2 is to be reduced to first-degree cosine terms, after which each
cosine term is to be multiplied by the modulus of c2, evaluated at the frequency or frequencies con-
tained in that term, and the phase angle of c2 is to be added to the phase of the cosine term. For
the method of assigning frequencies in c2 and cs see eqs. (19a) and (20a).
As in the case of resistance load the grid voltage eg does not equal the voltage introduced
into the grid circuit (<3'g), but can be obtained therefrom, as
- • - • (21)
in which z" is the total impedance of the grid circuit. In the second term (z")2 is to be
treated like the term (c)2 in eq. (19), that is evaluated at the separate frequencies which
are beating together.
For example, assume a pure cosine voltage e'p — E'ps cos (u8t + 08) impressed in the
plate circuit, and a similar voltage eg = Egn cos (coni + 0n) between grid and filament (or
anywhere in the grid circuit if the grid is held negative). Then as far as Ci and c2 are
concerned
^'gn COS (oant + I
^pa = :
9V) E'f, cos (ust + i
/32n)
'Z' (2s)
, cos (
[
r)
p8 cos
(22)
where *
= 8n - tan"1
• and 0% is similar
/52n « 20V — tan"1 X(2n) and /33a is similar
and
= 0V + 0'. = tan
= 0% — 0V - tan"1
* Note carefully the positive sign associated with tan
; in /35rt. This occurs through the
subtraction of B'n from 0'8, even though Zn is in the denominator. The importance of this difference
in sign of this term in (S^n and fi$n is brought out in Section 7, article 18.
METHOD OF SUCCESSIVE APPROXIMATIONS 5-45
A comparison of the expressions for ci and c2 given by eqs. (18) and (19), respectively,
shows the effect of the impedance load, which appears in the denominator of GZ to a higher
power, in decreasing the percentage value of the harmonic terms, or in straightening the
plate and mutual characteristics. From this it may be seen that an impedance load acts
similarly to a resistance load in tending to decrease the relative size of the harmonics intro-
duced by the non-linear shape of these characteristics. The impedance load of course
introduces frequency distortion.
DYNAMIC PLATE RESISTANCE. When the steady voltages applied to a triode are
such as to cause the static operating point to be within a curved region of the mutual
Cor other) characteristic, or so near to a curved portion that the applied alternating voltage
causes the triode to work on a curved portion for a part of a cycle, more accurate re-
sults will be obtained from the series expansion by evaluating the derivatives at the
average values of voltages obtaining during the cycle. These may be quite different from
the static values. The plate resistance so defined ( — = — ) is called the
\rp <ze&J average/
dynamic plate resistance; see eq. (12). All other derivatives should likewise be evaluated
at the dynamic operating point, if there is considerable change in the direct, or average,
current when the signal is impressed.
The dynamic parameters are quite tedious to compute but their values may be approx-
imately measured on an impedance bridge if the amplitude of the applied voltage is the
same as that of the signal voltage. The resistance measured on the bridge is called the
effective plate resistance and for small or medium voltages is equal to the dynamic plate
resistance. When they are not equal the dynamic resistance is the value to be used in
evaluating the series; the effective value must be used if it is desired to express all the
fundamental current in one term.
VARIATION OF AMPLIFICATION FACTOR. If the variation of /i must be con-
sidered (it always should be in pentodes) the first term (ci), Table 1, is unchanged but the
second term (02) is
which shows the increased distortion arising from the variation of ju.
22. ANALYSIS FOR MULTI-ELECTRODE TUBES
The above method of analysis can be extended to tetrodes, pentodes, etc. If voltage
is introduced into only one control circuit, and if the other grids have low impedance, the
analysis as given is sufficient for any case. If, however, there are impedance drops in
several of the electrode circuits each must be analyzed in the same manner. The equations
are very complicated and not of sufficiently general interest to be included here (see
High-Frequency Alternating Currents, McHwain and Brainerd, John Wiley & Sons, Appen-
dix A, for complete development).
23. METHOD OF SUCCESSIVE APPROXIMATIONS *
The calculation of the coefficients in the power series expansion of a vacuum tube and
its associated circuit becomes extremely complicated for terms higher than the third term
and for analyses of multi-electrode tubes. Thus the analysis of circuits containing vacuum
tubes by means of the Taylor's series expansion of the tube characteristics, although
theoretically applicable to all circuits, is applicable in practice only to those circuits for
which the series converges very rapidly. The factors affecting the convergence are (1) the
amplitude of the applied voltages and (2) the sharpness of the curvature of the character-
istic in the operating range, that is, the magnitude of the higher derivatives of the char-
acteristic. Thus for high level voltage amplifiers, power amplifiers, large signal detectors
(including linear detectors), and most oscillators, the treatment by Taylor's series is
practically useless except possibly for qualitative analysis.
In such cases the method of successive approximations is sometimes useful. Equations
of the form ,^ ,
2) (23a)
s) (236)
are written for the total number of currents and voltages involved.f
* Articles 23 and 24 were contributed by Dr. Carl C. Chambers.
f This method is applicable to certain types of discontinuous functions such as those found in dealing
•with gas-filled tubes.
5-46
ELECTRIC CIRCUITS, LINES, AND FIELDS
For the triode with voltages in both the plate and grid the equations become
ip = Fi({e'g - ig[ X z,]}, [e'9 - ip[ X zj}) (24o)
ig « ft({fl'* - « X zj}, {e'p - ip[ X zp]}) (246)
where the symbols have the same meaning as in the previous section on the Taylor's series
expansion of vacuum tubes.
The values of the resulting currents are estimated and called ipo and %)• These can be
obtained from oscillograms of a similar vacuum tube, from the approximate solution by
means of the Taylor's series expansion, or simply from an intuitive guess. Although the
accuracy of the estimate of the value of ipo and igQ is not theoretically important, the labor
involved is directly dependent upon this accuracy.
Having ipQ and igQ, the first approximation is calculated by substitution of these values
in the right-hand members of (24a) and (246), giving
*pi = Fi({St ~ »«o[ X zj}f {e'p - ipot X zp]})
igi = Fi({efg - igo( Xzg]}, {e'p - ipQ[ X zp]})
The second and higher order approximations are obtained by substituting the preceding
approximation in the right-hand members of eqs. (24).
In making these successive substitutions it is necessary to write the preceding approxi-
mation in separate sine-wave terms in order to evaluate igr[ X zj and ipr[ X zp]. This
can be done by any of the various methods for harmonic analysis (see Fisher-Hinnen,
Method and Wave Analysis, article 1) . When zp and zg are selective impedances, the only
harmonic components of the current of importance for purposes of substitution are those
for which zp and ze are not essentially zero. For this reason this method of analysis is
especially applicable to class B and class C r-f amplifiers, oscillators, and frequency
multipliers, where the plate impedances are highly selective.
The functions FI and F% can be in any form in which they are completely specified over
the entire operating range of the applied voltages. Thus any analytical expression for
the tube currents or any complete set of curves is sufficient for use in the above method of
analysis.
24. HARMONIC ANALYSIS OF THE CURRENT FOR A SINUSOIDAL
APPLIED VOLTAGE
In many cases the performance of a non-linear circuit can be predicted from a knowledge
of the harmonic content of the current when a sinusoidal voltage is impressed in the cir-
cuit. The usual discussion of the
merit of a non-selective amplifier as-
sumes a sine-wave excitation, to avoid
the complexity introduced by the
presence of the many beat terms
otherwise present.
When the relation between the in-
stantaneous impressed voltage and the
instantaneous current is given it is of
course possible to plot the wave form
of the current. This may then be
analyzed by any of the usual methods
of wave analysis.
When the input voltage varies sinu-
soidally, the output current will be
periodic, having a fundamental peri-
odicity equal to that of the input volt-
age. In resistive circuits the relation
between the input voltage and the
output current is independent of time,
so that the output current will pass
from maximum to minimum and from
minimum to maximum over the same
path, in fact, over the characteristic
curve. (The term characteristic is
FIG. 5. Tube Characteristic and Sine- wave Input
applied in its original sense to the instantaneous relation between input voltage and output
current). It follows that, if a complete period of the plate current is T seconds,
HARMONIC ANALYSIS OF THE CURRENT 5-47
= i(T — t) when the origin of time is chosen at the instant when the current is a max-
imum. This form of symmetry insures that when the output current due to a sinusoidal
input voltage is written in the form
i = Jo + Ii cos («« + ]8i) -h Ii cos (2otf -f &) + (25)
the phase angles /?i, £2, etc., will be zero.
Several methods of analysis are used to obtain the values Jo, Ii, etc. The one of broadest
application is the variation of the Fisher-Hinnen method applicable to such a characteristic
curve instead of to the wave itself. The analysis by this method can be stated as follows :
consider the zero point of the sinusoidal input voltage variation to be the zero of the base
line of the characteristic, and consider the scale along this base line to be such that the
peak value of the input voltage is unity. Then i(e) is the relation given by the mutual char-
acteristic where e is the input voltage which on this scale varies from — 1 to +1 and i is
the corresponding output current (see Fig. 5). Then the /'s to the second approximation
in the Fisher-Hi r>nen method of analysis are given by
11 = 1/2[*U) -*(-!)]
12 = 1/4 [i(l) - 2t(0) +**(-!)]
h = 1/6 [*(D - 2*(0.5) + 2i(-0.5) - *(-D]
I4 = i/8[»(l) - 2*(0.707) + 2i(0) - 2i(- 0.707)
In = 1 \iW-X (cos
2n L \w
The J's to the fourth approximation in the Fisher-Hinnen method are then given by
I'n = In - I2n - Ifa
The d-c component Io is given to the second approximation by
Jo _ Vl [i(0) + ^+;("1} + i(0-707)+;("°-707)]
Another method (see D. C. Espley, Proc. I.R.E., Vol. 21, 1439 [1933]) has the advantage
that the points along the input voltage axis of the mutual characteristic, at which the
current is evaluated, are equally spaced. This analysis using three points gives results
identically the same as the values for " Ii and /2 given by the Fisher-Hinnen method.
When five points are used the I's become
Jo = 1/6 fr'U) + 2t(0.5) + 2t(-0.5) + *'(-l)]
Ii = 1/« [*(D + *(0.5) - i(-0.5) - t(-l)]
I2= 1/4 [t(l) - 2i(0) +*(-!)]
Is = Ve WD - 2t(0.5) + 2i(-0.5) - *(-!)]
/4 = 1/12 [*(!) - 4i(0.5) + 6i(0) - 4£(-0.5) + *(-!)]
For the values of the I's using seven equally spaced points see the original paper referred
to above.
In the special case when the even harmonics are balanced out as in "back to back"
amplifiers (pushpull class A, class B audio, and class AB amplifiers, see Amplifiers, Section
7) the mutual characteristic becomes like that shown in Fig. 6. I0 is balanced out of the
output current as well as the even harmonics so that i(e) = —i(—e}. For such amplifiers
the analysis by the Fisher-Finn en method gives for the remaining I's
Ii = *(D
/s = 1/3 Pd) - 2^(0.5)]
Is = l/5 [i(l) - 2i(0.809) + 2t(0.309)]
I7 - 1/7 [t(l) - 2i(0.901) + 2i(0.624) - 2»(0.222)I
As before, a better approximation for In is obtained by subtracting I&n from the cal-
culated In.
5-48
ELECTRIC CIRCUITS, LINES, AND FIELDS
When this symmetry exists the method of Espley described above reduces to the Fisher-
Hinnen method when the measurements are made at only five points (for this special
case only two points need actually be measured), and the seven measured point analysis
of Espley reduces to
Ii = 1/320 [167i(l) 4- 252i(0.667) - 45^•(0.333)]
h = Vi28 [45i(l) - 36^(0.667) - 63i(0.333)]
IB = 8i/640 [>•(!) - 4^(0.667) + 5z(0.333)]
Here because of the symmetrical character of the curve only three points actually need
be measured.
Mouromtseff and Kozanowski (Proc. I.R.E., Vol. 22, 1090 [1934]) give a somewhat
simpler method to calculate up to the eleventh harmonic in the case of a symmetrical curve
such as Pig. 6. The straight line aob is drawn intersecting the curve at the point of maxi-
mum input voltage, that is, e — 1 in the notation used above. Then, instead of measuring
i(e), Ai(e) is measured where Ai(e) is the difference in current between the curve and the
line 006 and is taken positive when the line 006 is above the curve. This gives for the Pa
in the order in which they are to be calculated
IB = 0.4^(0.309) - At(0.809)]
J3 = 0.4475[Ai(0.309) + Ai(0.809)] + 0.333Ai(0.5) - 0.578Ai(0.866) - 0.5I6
IT = 0.4475[Ai(0.309) + At(0.809)] - Ji + 0.5J5
J9 * /3 - 0.667A*(0.5)
In = 0.707 A£(0.707) - J3 -f Is
Ji = i(l) - Ij + IB - IT + Is - In
Any of the above methods can be used for the calculation of the I's in eq. (25) when
the input voltage is sinusoidal. The per cent amplitude for any given harmonic is then
In/Ii for an input voltage, the peak value of which is taken e = 1. The complete equation
of the curve from e — —I to e — +1 can be written in the form
i(e) = IQ + lie + h cos 2(cos~1e) + Is cos 3(cos~1e) + • • •
This expression for the output current is unique; that is, for each value of e between
— 1 and + 1 this equation gives the corresponding instantaneous plate current provided
that the conditions prescribed at the
beginning of this section are fulfilled,
chiefly, that the load is essentially a
constant resistance over the operating
frequencies and voltages. This expres-
sion can be used in several ways although
calculations of the operation for input
voltages other than a simple sinusoid of
amplitude unity on the scale of e are
extremely complex analytically.
The calculation of the distortion and
output by any of the above methods for
a sinusoidal input voltage having an
amplitude of a fixed fraction of e can be
made by means of this expression for
Output
-1
Current
& — * Input Voltage
i(e) without again using the curve.
Formulas can be developed for this pur-
pose using any of the above methods of
analysis as a basis giving the I's corre-
sponding to an input voltage of frac-
'Back tional amplitude.
This method of analysis can generally
be used when the resistive load is-
coupled into the non-linear circuit by a transformer. For if the transformer is "perfect"
FIG. 6. Mutual Characteristics of Two Tubes
to Back"
the relation between voltage and current is the same as for a resistance load (see Trans-
formers, Section] 6) ; in other words the transformer offers a resistive impedance to the
circuit. Practical transformers are nearly perfect enough to assume that their only effect,
is to multiply (or divide) the load resistance by the square of the turn ratio.
ELECTROMAGNETIC RADIATION 5-49
25. INPUT IMPEDANCE OF A TRIODE
Neglecting the leakage resistances between electrodes the equivalent circuit of a triode
with grid negative is shown in Fig. 7. The equivalent input resistance is
C3-
(26o)
the equivalent input reactance by
f wVCCfl + C'sXr2 + a?) A + B(r* + re2 + rr.
) \
C3) (rp2 + rrp) - wrp2^(2A + C32) f
Tpl
Cz)}}\
where A « dC2 + dC3 + C2C3, and B = Ci -f C2 -f ^C3.
Both the numerator and denominator of each of these expressions contain negative
terms ; thus either can be positive or negative depending on the circuit parameters. If the
value of the reactance becomes positive it indicates that
the equivalent input reactance is inductive. If the value 1 G?d 1L iplatei
of the expression for resistance becomes negative, it in-
dicates that the real part of the input impedance of the
tube is an equivalent negative resistance and is supplying
instead of absorbing power. The input resistance will t
become negative only for certain values of inductive load; ' Filament
cf. eq. (26a). When this condition exists, the tube will -n, - 0. .._ , „ . . . ~.
, i . i . , . r .. TJ f FIG. 7. Simplified Equivalent Cir-
always supply a greater plate current than it would for cuft Of a Tnode
the same grid voltage and a non-reactive load. When
this occurs the tube is said to be regenerating (see Section S) . If the negative input resist-
ance exactly equals the external resistance the total resistance of the circuit is zero and
current can flow without a driving voltage; in such a case the tube is said to oscillate (see
Section 7, oscillators).
When the grid voltage is positive, grid current flows and the grid resistance is defined
by lA*£ = dis/deg. This is practically infinite when the grid is negative but may be quite
small when the grid is positive; in this latter case the interelectrode impedances are usually
negligible in comparison to it so that the input impedance of the triode is simply re.
BIBLIOGRAPHY
Byerly, W. E., Elements of Integral Calculus, p. 332. G. E. Stechert and Co.
Carson, J. R., A Theoretical Study of the Three-Element Vacuum Tube, Proc. I.R.E., April 1919.
Steinmetz, C. P., Engineering Mathematics, Chapter VI. McGraw-Hill.
Mcllwain, K., and J. G. Brainerd, High-frequency Alternating Currents, Chapter VI. John Wiley.
Terman, F, E., Radio Engineering. McGraw-Hill (1932).
Llewellyn, F. B., Operation of Thermionic Vacuum Tube Circuits, 5.S.T.J"., Vol. V, 433 (1926).
Barrow, W. L., Contribution to the Theory of Non-linear Circuits with Large Applied Voltages, Proc.
I.R.E., Vol. 22, No. 8, 964 (August 1934).
Byerly, W. E., Elementary Treatise on Fourier Series and Spherical, Cylindrical, and Ellipsoidal Har~
monies. Ginn (1902).
Jahnke. E,, and F. Emde, Tables of Functions with Formulae and Curves, 2nd Ed., p. 242. B. G. Teubner,,
Berlin (1933).
ELECTROMAGNETIC RADIATION
By Knox Mcllwain
All forms of wireless or radio transmission depend on the fact that electromagnetic
energy is radiated from any wire in which a varying current flows. The current in the-
wire sets up magnetic and electric fields, in which it is usually assumed that the energy
associated with the current flow is stored; a portion of this energy, however, is not stored,
but continually travels away from the wire, or is radiated. Radiation is a phenomenon.
which is totally negligible at low frequencies.
5-50 ELECTRIC CIRCUITS, LINES, AND FIELDS
26. MAXWELL'S EQUATIONS
There are two well-known experimental relations between magnetic and electric fields.
The two fields are interdependent, a change in one always being accompanied by a change
of the other. The two laws are:
1. Whenever the net magnetic flux linking any closed loop changes, an electromotive
force is set up in the loop. If 4> is the net magnetic flux linking the loop, then (Faraday's
law) the electromotive force is
•--2
2. The resultant ma|netomotive force (in ampere-turns) acting around any closed loop
is equal to the rate of flow of electricity through the surface bounded by the loop plus the
time rate of change of electric flux through this surface. If i = dq/dt is the rate of flow of
electricity (total conduction current in amperes) and ^ the electric flux through the surface
then the magnetomotive force is
dd
m = ^ + — (2)
at
Both these relations are such that the force expressed by the left side of the equation
bears a right-hand-screw relation to a positive increment of the right-hand side. They
apply to any medium whatever, to conductors, dielectrics, ferromagnetic substances, etc.
By applying these equations to an elementary volume in space, Maxwell's laws of
electromagnetism are developed. Stated in vector notation these are (all quantities are
expressed in mks units)
dH An
— ju — - = curl £ (4)
at
From these the continuity equations immediately follow;
div u — 0 (5)
div B = 0 (6)
where u is the total current density in amperes per square meter and B the magnetic flux
•density in webers per square meter.
Stated hi the ordinary component form these equations are:
(3a)
(36)
(3c)
(4a)
(46)
dDx , , y , , n ,K .
(5a)
-where <r is the conduction current density in amperes per square meter and D the electric
.flux density in coulombs per square meter, and
^ + ^2 + ^ = 0 (to)
dx dy dz
'Only fields which satisfy these relations are possible, and these equations may be used to
-determine the necessary form for particular fields.
PROGRESSIVE PLANE WAVES 5-51
The energy flow associated with the electromagnetic wave is found by developing
Poynting's vector
P = e#sin(£, H) (7)
which is a vector perpendicular to 8 and H, whose magnitude depends on the product of
e and H and the sine of the angle between them (measured counterclockwise from £ to H) .
The integral of Poynting's vector over a surface gives the rate at which energy flows
through the surface.
WAVE EQUATION. In an isotropic insulating medium no conduction current can
flow, since 7 (eq. 3) is zero. Elimination of H between eqs. (3 and 4), and similarly for £,
gives the wave equations
*?_ J_ /*? + ££ + d^
df ~ V.K W + w + a?
Solution of these equations shows that each component of electric or magnetic field must
have the form
where v = ±l/Vju5. These functions represent incident and reflected waves (see p. 5-23)
traveling at the velocity v ( = 3 X 10s meters per sec in vacuum and close to that in air) .
The wavelength is defined as the distance traveled in. one period.
27. PROGRESSIVE PLANE WAVES
The simplest form of wave mathematically is one which travels along the x axis, say,
and in which it is assumed that none of the fields vary with y or 2, In such case (by
Maxwell's laws)
e* = 0 (lla)
Sy = 8y COS CO (t - - J (116)
e, == e* cos
Hx = 0 (lid)
pr A/_±. $?
jti 2 — V — C-y
in which co = 2-n-/. Then «[* - (x/a)] = wt - 2irx/\.
In the general form the loci of the vectors e and JT are ellipses, so that the plane wave
above is said to be elliptically polarized. If ey = Bz and dz — ir/2 or 37T/2 the ellipse reduces
to a circle and the wave is said to be circularly polarized.
If either sv or ez is zero, or if dz — 0 or TT, the ellipse reduces to a straight line, in which
case the wave is called a plane-polarized wave. The electric energy per meter3 of such a
wave at any point in the field is 2?e2/2, and the magnetic energy per meter3 is jufir2/2.
It follows that for a progressive plane-polarized wave at every point the total energy is
always half electric and half magnetic, but its value varies, of course, with position and
time. The total energy (W) of the field is
W = We + Wm = K&dr (12)
where dr is an element of volume. The average energy is Wi — Xe2/2T and the average
rate at which energy passes through a meter2 in the YZ plane is
5-52 ELECTRIC CIRCUITS, LINES, AND FIELDS
28. FIELDS DUE TO A CURRENT IN A WIRE
If a current i flows in a short length of wire (see Fig. 1) located in free space and assumed
at the origin of coordinates and coincident with the z axis, the fields at any point P(x, y, z)
are
- - *&
*-
(WC)
J-T-
dydt
Hz = 0 (14/)
where w ^ -fi [ t — «- ) ; in this expression d is the distance from the origin to the point,
d \ v
and Fi(t) expresses the distribution of charge in the wire, so that F(t) = idl, where 81 is
the length of the wire (assuming uniform current for the differential length 81) .
If the current is assumed sinusoidal, so that i = V2I sin (ut + 90°) amperes, at any
point distant from the wire (so that d ^> X/2?r) , the fields are
cos 6 cos (ut — pd) volts per meter (15a)
,^ „
150 aA
COs 6 cos (w£ — (3d) ampere-turns per meter
where 6 is the angle of elevation of the point P from a plane perpendicular to the wire.
All lengths are expressed in meters.
The direction, of the electric field is perpendicular to d and in the plane formed by d
and the axis of the wire. The magnetic field is perpendicular to d and the electric field.
Such an elementary wire is called an electric doublet. The fields due to a long length
of wire I can be obtained by integration of the elementary length (see Antennas, Section 6.)
The average rate of flow of energy per square meter through
an area perpendicular to d is (in watts)
and the total power radiated (in watts) is
FIG. 1. Elementary Radi- p_ _ ?!-
ator rr ~ \2
The radiated power for a given current varies directly as 1/X2 or as the square of the
frequency. For a given total charge, or a given voltage difference between the ends of the
antenna, the radiated power varies as 1/X* or as the fourth power of the frequency.
29. REFLECTION AND REFRACTION
Whenever an electromagnetic wave meets a boundary between two media of different
dielectric or magnetic properties, there is a change in the fields and frequently the wave
splits into two waves, one of which is reflected back into the first medium, the other is
refracted into the second medium.
CONDITIONS AT THE BOUNDARY. The following proposition is assumed: In two
media, the components of the electric (or magnetic) intensity tangent to the surface sepa-
rating those media are equal (in magnitude and direction) at this surface. It follows from
REFLECTION AND REFRACTION
5-53
this that the normal component
of the surface, that isr UN — u^
Similarly
of the total current density is the same on both sides
or for insulating media
DN — D^N
The general expression for a plane wave as far as £ is concerned is:
£x COS OJ I t
8y J
co f i - -j -f 5*
(18)
(19)
(20<z)
(206)
(20c)
where 5y and 5Z are constants and &x is the maximum value of the X component of £.
TWO ISOTROPIC DIELECTRICS. Consider two media separated by a plane sur-
face, and assume that a plane wave in medium 1 impinges on this surface (see Fig. 2).
Assume that the total electric intensity £ in the first medium is composed of two parts
£1 and £'i; then
£ = £1 + £'i (21)
£1 will be called the incident wave (see also p. 5-23) and £'i the reflected wave; £'i will have
components similar to those of eq. (20) denoted by prunes. Note that, 3/1 being undeter-
mined, what is called the reflected wave is not restricted to travel in a direction directly
opposite the incident wave, as is
the case on transmission lines.
Assume that the resultant elec-
tric intensity in the second medium
is £2, called the refracted wave,
with similar components identified
by the subscript 2.
Applying Maxwell's equations
at the boundary, &I-QI — /3'ifl'i =
182^2 or coi = oo 'i = co2» so that all
waves have the same frequency.
Also the incident, reflected, and
refracted waves all have wave nor- ' ~Y Origin is at 0
mals (perpendiculars to the wave FIG. 2. Wave Normals
front) in the same plane. Similarly
if 0 is the angle between the wave normal and the normal to the boundary then «
or the angle of incidence is equal to the angle of reflection. Also
Normal to
Interface Between
Two Media
Normal to Wave Front
of Incident Wave, or
Incident Wave Mojcmal
sin (£2
: - = f\
(22)
where TJ is the relative index of refraction of medium 2 with respect to medium 1.
The magnetic intensities of the various waves are, in magnitude (from Maxwell's
equations), HI = V ' K\l Vi£i, Hfi ~ v'JSi/juie'i, and #2 — V Kz/^fy. All these are vectors
in the wave fronts such that £1, Hi, and pi are mutually perpendicular in such orientation
that rotation from £1 to HI (through the smaller angle) would move a right-handed screw
in the direction of p.
Normal Components. It is convenient to split the electric and magnetic intensities into
two components, one normal to the plane of incidence (not the interface between the media)
and one in the plane of incidence. Maxwell's equations apply to each separately, since
the equations are assumed linear (there has been some indication, the intermodulation of
waves in space, that the equations are not entirely linear) . The normal components, at
the interface in terms of the incident wave, are
Z'IN ,~, cos fa VT^T — cos c})2 '
/8'iN =
822V
—
2 cos <£i '
+ cos
(23a)
(236)
5-54
ELECTRIC CIRCUITS, LINES, AND FIELDS
Since cos fa = Vl — sin.2 <fe and since sin 0i/sin fa = T\ (the index of refraction) , then
cos 02 = Vl — sin2 0i/V Hence, if sin 0i > 77, cos $2 will be imaginary. This is the case
of total reflection (see below) . The angle of incidence for which sin 0! = 77 is called the
critical angle,
Parallel Components. The parallel components at the interface, in terms of the inci-
dent wave, are
S'IP e'iP /B/ cos 0i
- — = = — /5'ip =
£lP 8lP
82P 82P /s
- = =— /Q2P
8lP 81P
COS 01 VfJLlKz + COS 02
2 COS 01 VfJL^Ki
-
(246)
cos 0]. V Ml#2 + COS
Case of Total Reflection. If cos 02 is imaginary let cos 02 = jn^ where n^ is the absolute
value of the imaginary. Substituting this in eqs. (23) and (24) , the normal components are
cos 0i
COS 01
(25)
and the parallel components are
cos 0i
Refracted
Beam
X There is a disturbance in the second medium but no
energy is transmitted, so that the wave is said to be
totally reflected.
Energy Relations. To compare the energy in the
Incident incident, reflected, and refracted waves determine the
Beam rate at which energy is delivered by the incident wave
to a certain area of the surface separating the two media,
and the rates at which it leaves this area in the reflected
and refracted waves (see Fig. 3) .
The respective energies are
Incident beam: cos 0i dS V— 8i2 = \/— 8i2d£i
^ u v
Reflected beam: cos 0i dS
f^" S"
A/— e'i2 = \~
V *
Refracted beam: cos 02 d>S
— 822
— ~ 822d>Si
(27a)
(276)
(27c)
i cos 0i
The ratio of reflected to incident energy is eV/ei2, and of refracted to the incident energy
-
energy is
"^ — ( =• I »
KIM Vei/
where the 8's are evaluated at the interface.
cos 0i
Rotation of Plane of Polarization. If the incident wave is a plane-polarized wave, and
the plane of polarization (which contains HI and hence is perpendicular to Ci) makes an
angle 0i with the plane of incidence, then the angle between the plane of polarization and
the plane of incidence of the reflected wave (0'i) is
and for the reflected wave
tanfc
(28)
(29)
1 - 02)
When 0 < &i < Tr/2, the plane of polarization of the reflected wave is rotated toward the
plane of incidence, while that of the refracted wave is rotated away from the plane of
incidence.
REFLECTION AND REFRACTION 5-55
CASE OF A CONDUCTING MEDIUM. If a medium is conducting, its conductivity
is not zero, and by Maxwell's first equation (p. 5-50).
T£ + -j- = curl H (30)
where all quantities are in mks units. Assuming £ to be a harmonic function, it can be
written £ = / (xyz) £/w* and d£/dt = /co£. Hence eq. (30) becomes
-^ = curl H (31)
This equation is similar to that for a dielectric, the only difference mathematically being
that the coefficient of dt/dt is the constant K, whereas in eq. (31) it is the constant
K — JT/W. Hence all results obtained for insulating media are applicable to a conducting
medium provided the K used in the former case is replaced by K — jj/u.
If 8 = ~£ie~~ax*?(>Cj*t-px')i -which is a damped plane wave propagated in the X direction
with velocity co//3 and attenuation a. per unit length, then for this to be a solution of
./ry\ 52e
i - 3 — ) 8 = — ^
co / d^
(32)
(wave equation, all parameters are those of the conducting medium) it is necessary that
a = 2/ryfl. For good conductors y is large, hence a. is large and the wave is highly atten-
uated — good conductors are poor transmitters of electromagnetic waves. Indeed, a
perfect conductor (j = oo) will not transmit. These results hold for wavelengths not
near the visible-light range when the conductor (called in this case a reflector) is an ordi-
nary metal.
REFLECTION FROM A CONDUCTOR. If a wave traveling through an insulating
medium (1) strikes the (plane) interface of an adjacent uniform conducting medium (2)
all the results previously obtained for the case of two insulating media are applicable
provided Ki is replaced by K'z — jy/u, where K'% now represents the dielectric constant
of the conducting medium. Assuming directions shown in Fig. 2, a plane wave in the
insulating medium produces in the conducting medium a wave
g2 = e2eaVffa)* ~ 0'2 fr sin *'2 ~ 2 cos *'a) + *2 J (33)
where a is a positive real quantity (z is negative so the wave is damped) and to, £'2, ^'2,
and 52 are all real. The quantity w is 2-rrf where / is the frequency of the incident wave,
and 7/2, the velocity of the wave in the conducting medium, is w/P'z. Furthermore,
£'2 = 27r/X/2, where X'g is the wavelength of the wave, and
/ - - = /04.x
17 " V2 fa sin 0'2 ^ ;
is the refractive index of medium 2 with respect to medium 1. The various quantities
a, j372, sin ^'2, cos ^'2, 2/2, and if are all functions of the angle of incidence <fo. It is customary,
when not otherwise specified, to assume that quoted values of a, £'2, 3/2, and 17' are for
normal incidence (<fo = 0). To compute these quantities for any angle of incidence,
the following procedure may be used (K is written for Kfz and subscript N refers to normal
incidence; T to 27r/cj). Calculate or measure
Then 77' can be found from
and 1/2, P'z, and $'2 follow from eq. (34). The following are of importance:
^/rK7z only when jT is small and K\ = 1
i when yT ^> 1
when yT ^> 1
when yT ^> 1
5-56
ELECTRIC CIRCUITS, LINES, AND FIELDS
The ratio of energy reflected from to energy incident upon the interface per unit time is
e - (2/V-yT cos <fr) for yT large.
As 7 approaches oo, this ratio approaches unity, showing that good conductors are good
reflectors. For normal incidence (<£i = 0) it becomes
and in general, assuming
, it is
(m - ^
(ni +
+
It may be noted that in a conducting medium neither the electric nor the magnetic
vector lies in the wave front.
The preceding discussion has assumed K'% a constant, whereas it is sometimes necessary
(e.g., in Heaviside layer studies) to consider K'% and other quantities as varying.
BIBLIOGRAPHY
Ramo, S.f and J. R. WMnnery, Fields and Waves in Modern Radio. John Wiley (1944).
Skilling, H. H., Fundamentals of Electric Waves. John Wiley (1942).
Stratton, J. A., Electromagnetic Theory. McGraw-Hill (1941).
Schelkunoff, S. A., Electromagnetic Waves. D. Van Nostrand (1943).
Slater, J. C., Microwave Transmission. McGraw-Hill (1942).
ELECTROMECHANICAL SYSTEMS
By Knoz Mcllwain
Support
Vibrations in one dimension occur frequently in systems made up of solid elements, such
as a spring suspension, a pendulum, or a rocking lever. They occur occasionally in fluids,
an example being the transmission of sound through a long narrow tube. Alternating
electric currents in short wires will be shown to be similar analytically to unidimensional
mechanical vibrations. Also devices are in common usage (microphones, speakers, etc.)
which convert any of these forms of vibration into any other.
Because of the analytical similarity of the three forms of vibration, mathematical
results obtained in one field may be used in solving problems in the other fields. The
mathematics involved, such as the complex notation, has been applied more generally to
the electrical problem than to the others, but once the analytical similarity is established
advances in one field are immediately applicable to the others.
As a first approximation all the parameters are considered constants. This is reasonably
true in many electrical circuits but is not generally so in mechanical systems. However,
the variations for small displacements and ve-
locities such as occur in mechanical systems used
in acoustics are usually negligible. The methods
of attack available when the variation of param-
eters must be considered are given in articles
16-24.
DEFINITIONS. The number of independent
variables required completely to specify the
motion of every part of a vibrating system is a
measure of the number of degrees of freedom of
the system. When only one variable is needed
the system is said to have one degree of free-
dom; examples of such systems are (Fig. 1): a
piston moving in a cylinder, a weight hanging
from a spring, cylinder rolling on a plane surface
(no slipping). Systems of two or more degrees
of freedom are exemplified by an automobile moving on a plane (two degrees if no skid-
ding, three if skidding occurs), a balloon (three degrees if there is no spinning of the
balloon), an airplane (six degrees if rotation is considered), a set of weights connected
by springs in series (Fig. 2) which has as many degrees of freedom as there are springs;
continuous vibrating systems (waves traveling along a long spring or stretched string)
have an infinite number of degrees of freedom.
Equilibrium
• Position of
M
(a) Simple Mechanical (
System
FIG. 1.
"&) Electrical System
"Equivalent" to
Mechanical System
of (a) -
Electrical and Mechanical Systems
of One Degree of Freedom
ENERGY OF MECHANICAL AND ELECTRICAL SYSTEMS 5-57
Consider a system of one degree of freedom (Fig. 1) , and let the displacement coordinate
be chosen to measure the distance from the center of the mass M to the equilibrium posi-
tion. Consider that the spring has mass. The velocity of any given elementary mass of
the system will then be proportional to ds/dt( = s), so that the kinetic energy of this
elementary mass dm will be */2 ki&dmi, where ki is a constant dependent on the position
of the mass. Likewise the kinetic energy of any other elementary mass dm* will be
z, etc., and the total kinetic energy T of the system will be the sum of these, or
T - i/zfh's2 dim = 1/2 a* fki dmi (1)
where the integration is to extend over the entire mass composing the system. But
Jki dmi - mm (2)
where mm is a constant, called the generalized mass. Note that the value of mm depends
on the k's, which in turn depend on the choice of the measure of displacement. This
ffc)
FIG. 2. Mechanical System of Two Degrees of Freedom and Electrical Equivalent
choice is largely arbitrary, and the particular one here chosen may not be the most con-
venient. The factors entering the problem which depend on this arbitrary choice are
termed generalized. Thus s is a generalized velocity of the system; in this case it is the
actual velocity of the mass M, but need not be. On the other hand, mm is not the actual
mass of the system but might be made so with a proper choice of s, the generalized ^dis-
placement.
30. ENERGY OF MECHANICAL AND ELECTRICAL SYSTEMS
LINEAR MOTION. The kinetic energy of a mechanical system of one degree of
freedom in linear motion is
.(3)
where mm is the generalized mass of the system and s is the generalized velocity. The
generalized mass can be defined as the quotient of the kinetic energy T of the system
divided by the square of the generalized velocity.
The potential energy V of the system is a function of the displacement of the various
parts of the system; it is independent of velocity, acceleration, etc., and in a system of
one degree of freedom, since the displacements of the various parts are all proportional
to the generalized displacement s, the potential energy V is a function of s only, that is
V = V(s) (4)
This can be expanded in a Taylor's series:
where VQ is the value of V when s = 0, and the subscript 0 indicates that derivatives are
to be evaluated at s = 0. Since potential energy can be measured from any arbitrary
level, VQ may be taken as zero without loss of generality. Furthermore, in vibrating sys-
tems the generalized displacement may be so chosen that s = 0 for equilibrium; then, since
dV/ds = 0 for equilibrium, the second term on the right-hand side of eq. (5) drops out.
Making the further assumption that terms containing higher powers of s than the second are
negligible in eq. (5), V reduces to
where Cm is a constant ( — = -r-r- ). Cm is called the compliance; its reciprocal, the
\Cm oV Jo/
stiffness. It will be shown later that eq. (6) is equivalent to assuming that the restoring
forces of the system obey Hooke's law.
5-58 ELECTRIC CIRCUITS, LINES, AND FIELDS
If there is dissipation (heat) in the mechanical system, assume that the rate of energy
dissipation D is
D = r^s2 (7)
where rm is a constant.
In many mechanical systems, particularly those concerned with the small motions usual
in acoustic work, this is practically true; it is equivalent, as shown below, to assuming
that the retarding frictional force is proportional to velocity, and for small motions this
is approximately true of air friction. rm is called mechanical resistance. If it is not a
constant, that is, if D is not proportional to s2, but depends on higher powers of s as well,
the equations cease to be linear and the methods of articles 16-20 must be used.
ROTATIONAL MOTION. The kinetic energy of a mechanical system of one degree
of freedom in rotational motion is
T = W# (8)
where I is the moment of inertia of the system, <£ the angular displacement in radians,
and <}> the angular velocity in radians per second.
The potential energy is
"-!!
where the same assumptions regarding higher powers of <j> are made as in the case of
linear motion.
Likewise the dissipation is assumed as
D = rr<p* (10)
where rr is a constant.
ELECTRIC CURRENTS. The stored energy in an inductance L in an electrical
circuit is (cf . eq. [3])
T = i/aL* - i/2L^ (11)
where i(= dq/dt s q) is the current in the electric circuit, and q is the charge. This is
often called the kinetic energy of the electrical circuit.
The energy in a condenser C is (cf . eq. [6])
y-£S
The rate of energy dissipation in an electrical circuit is (cf . eq. [7])
D = ri*2 (13)
where r is the resistance of the circuit.
31. VIBRATIONS OF A SYSTEM OF ONE DEGREE OF FREEDOM
LINEAR MOTION. If a mechanical system of one degree of freedom is in a condition
of stable vibration its gains and losses of energy must be equal. Hence the increase in
kinetic and potential energy added to the energy dissipated must equal the work done, or
+ «V2Cm + frj? dt = fs (14)
-where fs, the product of force and distance, is the work done on the system. The rate of
o change of energy is
+ rms + s/Cm - / (15)
'Equation (15) is an equation in forces; that is, each term has the dimensions of a force.
'The first term, ras, represents the usual inertia! force due to the motion of the system; the
: second term, rms, represents a retarding force, proportional to the velocity of the system —
^this for small displacements and velocities represents approximately air friction, etc.; the
'third term, s/Cmi represents a force within the system proportional to the displacement.
'This last force is usually a restoring force, for example, the restoring force of a spring.
I Since this force is proportional to the displacement, Hooke's law (that the stress is equal
to the strain) applies. Any internal force, such as the restoring force accompanying the
; straining of any part of the mechanical system, so long as the part is not stretched beyond
the elastic limit, that is, so long as the restoring force is proportional to the displacement,
• contributes a term of the form s/Cm. On the other hand, if, instead of a restoring force,
• the term s/Cm were to represent a force proportional to the displacement, but tending not
i to issfcpBe. the system to its equilibrium position but to displace the system further, then
COMPARISON OF MECHANICAL, ELECTRICAL SYSTEMS 5-59
Cm would be intrinsically negative. There is no simple analog in a passive electric circuit
to this negative Cm which sometimes appears in mechanical systems. A "negative con-
denser" must be used, such as can be obtained in vacuum-tube circuits.
Equation (15) would be the equation of the system of Fig. 1, if the force were applied
to the mass M and if s were measured from the equilibrium position. The force / is a
function of i; it can be expanded in a Fourier series (see article 2) and each component of
Form F^*** treated separately. If s = sj0* then
srm 4- j'wwi™ +
and 5 = F/juzm, where zm = rm + jumm 4- l/jwCm is called the vector mechanical imped-
ance of the mechanical system. The real part of zm is the mechanical resistance; the
imaginary part is the mechanical reactance. If I were determined instead of s, assuming
s = s^wt, then s = F/zm. This is identical in form with the usual equation for a sine- wave
current in an electric circuit.
ROTATIONAL MOTION. The above analysis can be applied to rotational motion
if torque is substituted for force. Thus
rrtp + I^ + ^-L (17)
at LT
so that <}> = L/z, where z = rr + /[«/ — (l/wCr)] is called the vector rotational impedance
of the system.
32. COMPARISON OF MECHANICAL AND ELECTRICAL SYSTEMS
UNITS. The analogy developed above between the equations of mechanical systems
and electric circuits must not be interpreted to mean that there is any actual similarity or
analogy between quantities occupying the same position in their respective equations.
The inertia of the electric circuit and the mass of the mechanical system though appearing
in the same place in the differential equation are otherwise quite diverse. Perhaps the
difference is most convincingly shown by the fact that the analogous quantities current
and velocity have different dimensions, current having the dimensions M^L^T~l in the
practical electric system whereas the dimensions of velocity are LT~l.
If this difference is kept in mind and it is remembered that the analogy is merely a
formal one, representing the similarity of the differential equations expressing the be-
havior of the several systems, it is convenient to draw analogies between all quantities
of the several systems. A list of these is given in Table 1. Any system of units may be
used in any of the equations; only the cgs mechanical systems and the practical system
for the electric circuit are shown in Table 1 on p. 5-60.
When energy equations are written in the two systems the dimensions of the equations
must of course be identical, since the dimensions of energy are fixed. The usual current-
electromotive force equation, however, does not have the same dimensions as a mechani-
cal force-velocity equation. Nevertheless it is perfectly proper to set up electric circuits
which are equivalent to mechanical systems, or vice versa, use the ordinary electric mesh
equations to obtain a solution, and use this solution to specify the proper constants for
either or both systems. The validity of this procedure depends on the fact that the solu-
tion of the differential equations is independent of the meaning attached to the symbols.
SYSTEMS OF MANY DEGREES OF FREEDOM. The extension of the analogy
between electrical and mechanical systems to more than one degree of freedom, and the
analysis of such systems which contain both electrical and mechanical portions, are most
readily accomplished by the application of Lagrange's principle. In the application of
this principle the energy equations for the whole system are first written down, in terms
of measurements from an equilibrium position. Lagrange's equation that
d BT d(T - V) 1 dD _
dft 2 da Jl ^ '
is applied for each independent coordinate (each q needed in writing the energy equations).
ELECTRICAL CIRCUITS EQUIVALENT TO MECHANICAL SYSTEMS. If the
energy equations of two systems can be thrown into the same form then the solutions
of the two systems must be identical. The same applies to the differential equations, or
to the resulting mesh equations, but in general the similarity of the systems can be estab-
lished more readily by use of the energy equations.
5-60
ELECTRIC CIRCUITS, LINES, AND FIELDS
Table 1. Analogous Quantities in Linear and Rotational Mechanical Systems and
Electric Circuits
The cgs units and practical electrical units are used.
LINEAB MOTION
ROTATIONAL MOTION
ELECTRIC CIRCUIT
Quantity
Unit
Sym-
bol
Quantity
Unit
Sym-
bol
Quantity
Unit
Sym-
bol
Force
dyne
/
Torque
dyne cm
L
Electromo-
tive force . .
volt
e
Displacement
cm
s
Angular
displacement
radian
<f>
Charge .
coulomb
Q.
Velocity
cms
s
Angular
velocity ....
radian
4>
Current ....
ampere
i
sec
sec
gram
mm
Moment of
inertia
gram cm2
I
Inductance. .
henry
L
Linear
cms
cm
Rotational
compliance .
radians
Cr
Capacitance
farad
C
compliance
dyne
dyne cm
Mechanical
resistance. .
dyne sec
cm
mech.ohm
rm
Rotational
resistance. . .
dyne cm sec
rr
Resistance . .
ohm
r
radian
rotational ohm
Mechanical
reactance. .
ohm
*m
Rotational
reactance. . .
ohm
xr
Reactance . .
ohm
X
Mechanical
impedance.
ohm
Zm
Rotational
impedance. .
ohm
ZT
Impedance
ohm
z
p
ergs
sec
Pm
Power . . • •
ergs
sec
Pr
watts
P
The rules for establishing the equivalence of an electric circuit with a mechanical
system are therefore:
1. Write the equations for the kinetic energy, the potential energy, and the dissipation
of the mechanical system.
2. There will be an electric mesh for each independent generalized coordinate.
3. Any parameter which appears in an energy equation multiplied only by the square
of one generalized coordinate is a part of the corresponding electric mesh, and is not
common to any other mesh.
4. Any parameter which appears multiplied by the difference of two generalized coordi-
nates will be common to the corresponding electric meshes.
5. Any parameter which appears multiplied by the product of two generalized velocities
may be represented by a mutual inductance between the corresponding electric meshes.
6. If parameters appear in the energy equations multiplied by any other combinations
of the generalized coordinates, new coordinates should be chosen in an attempt to eliminate
them. If this is impossible * there is no one-to-one (parameter-to-parameter) equivalent
circuit.
To illustrate the method two examples will be worked out.
In the mechanical system shown in Fig. 2 (a) assume that the masses MI and M% are
resting on a plane surface whose frictional force is proportional to velocity. Let Si and S2
be the changes in s'i and s'a from the equilibrium position. Then
T =
S2)2
and
2 Cm
* Such cases will not be frequent. When encountered it is best to write force equations and attempt
to obtain circuits which will represent the mechanical system by allowing electrical parameters to
represent combinations of mechanical constants; for example, Z/2 = 2m2 + mi or C$ = Cm\ — Cm4
-f- Cms might be required. In many such cases the utility of the method is doubtful.
COMPARISON OF MECHANICAL, ELECTRICAL SYSTEMS 5-61
The equations for T and D both contain a parameter multiplied by the sum of two gen-
eralized velocities squared, for which no electrical equivalent is given in the usual simple
rules for independent meshes. These equations may be altered in two ways; first, the
direction in which s'2 (or s'i) is measured may be changed; or second, new s's may be chosen.
If the first alternative is employed
V is unchanged and
T -
D =
The equivalent electrical circuit is shown, in which LI — MI, L2 = M^ r\ = rmi, r% = rm2l
d SB Cmi and Cz = Cm2. That is, in the electrical circuit 1 henry of inductance is specified
for each gram of mass in the mechanical system, 1 farad of capacitance for each centi-
meter/dyne of compliance, etc.
V 2 CW
Cm2
FIG. 3. Same Mechanical System as Fig. 2 and Alternate Electrical Equivalent
If the second alternative is chosen the sketch of Fig. 3 would represent the conditions.
Here
1 (s2 — si)2
'2"
and
D =
The corresponding electric circuit is shown.
It is thus possible to have more than one equivalent electric circuit for a given mechan-
ical system, depending on the choice of independent variables for the mechanical system.
Casual examination of the electric circuits reveals them as equivalent, in that although
the mesh currents differ the current through any element would be the same.
FIG. 4. Mechanical System of Four Degrees of Freedom and Electrical Low-pass Filter
In the mechanical system shown in Fig. 4 first assume that the displacements are
measured between masses, as in Fig. 2. The energy equations are
T =
2
and
In this case it is impossible to throw the equations into the usual mesh equation form by
changing the direction of measurement of one or more of the variables, so the variables
must be changed if the convenience of the mesh equation technique is to be utilized. If
the system used in Fig. 3 is assumed
T - lyWi^i2 + i/2^22 + VaAfjA2 +
2
- Si)2
and
The equivalent electric circuit is a low-pass filter as shown.
5-62
ELECTKIC CIRCUITS, LINES, AND FIELDS
33. ELECTROMECHANICAL-ACOUSTIC SYSTEMS
Many vibrating systems consist of combinations of two or more of the separate energy
systems discussed above. Examples of such combinations are electrically controlled vi-
brating reeds and tuning forks, microphones and speakers of all varieties, fluid-type auto-
mobile stabilizers, and almost all musical instruments.
In such systems energy is converted from one form to another within the system. The
methods of converting energy are many, so that the forms of the interaction between the
different portions of the system are many, but the same general method of deterrnining
the force equations that was used for homogeneous systems can be applied.
The energy of each portion of the system should be set up exactly as for a homogeneous
system in terms of the constants of the particular portion. Some of these constants will
be functions of the velocity or displacement, etc., of some other portion of the system,
and these must be so specified. Then the "force" equations may be obtained directly by
means of Lagrange's equation, and from these the mesh equations may be written. These
mesh equations will not usually be of the same dimensions, but this fact may be disregarded
since the interaction factors between the equations will be such that when the equations
are solved simultaneously these differences will be automatically compensated. One set
of self-consistent units is shown in Table 2. Several particular cases will be developed
to show the operation of the method.
ELECTROMECHANICAL SYSTEMS, ELECTROSTATICALLY COUPLED. Con-
sider a system consisting of two metal plates, one fixed and immovable, the other held in
position by a spring (cf. Fig. 5) and resting on a rough surface. An electric circuit con-
nected between the two plates contains an inductance, a resistance, and a source of voltage.
Equilibrium
FIG. 5. Electromechanical System, Electrostatically Coupled
The potential energy Vm stored in the spring (measuring energy from its value at the
equilibrium position, when the electric charge is zero) is
7 =!-*
m 2Cm
where Cm is the compliance of the spring and $2 is the distance the spring is stretched by
moving the movable plate toward the fixed plate.
The potential energy Ve stored in the condenser is
where q is the charge on the condenser and C its capacitance. The value of C is
c_ kS = C'
47r(s0 - s2) s0 — $2
where k is the dielectric constant, S the cross-section of the plates, and (so — s) the distance
between them.
The kinetic energy of the system is
m*l Lf
2^2
where m is the generalized mass of the movable plate and spring together and L is the
inductance of the electrical system. The dissipation of the system is
D = rJ2 ri?
ELECTROMECHANICAL-ACOUSTIC SYSTEMS
5-63
*•
.£
<!
o
to
I
B
a
J2
•a
P
"5
1
S-3
09
.«
*?
£»
5-
^
»•
5-
£
^
r-
e-
0
+-
Q
s
*3
o
1—1
2 s
vx
A *p
to
"3
S
00
X
X
O
° o
° o
^f
(H
CQ
P
s
o
1
I
o 1
i I
|X
o
-*a '-'
|X
*
|i"
£
-&
ef
d
Jl
p
^
1
I
©
8
:
©
If
S3
Displacem
Particle ve
a S'fl
^§.2
i
i
=3,
11
E°
Acoustic
resistance
Acoustic
reactance
.s|
j!
g
1
*^j O
2j
T3 43
a-s
0*
•r*
w
M
0
o
<3
.
a.?
ss
CQ
^s
Fi
?^
P
8
6
P
1
1
O
!
"3
C
o
1
S
J
o
£
•§
03
given i
m is on<
o
-S^3
J
Quantity
W
a
Current
Voltage
Inductance, . .
|
0
0
V
1
Reactance
Impedance. . ,
0
flf
mto set of unite
A rotational
1-
-s-
-6-
^
-
*
-
*
*
*
if
r-
^
0
•*!
TIONAL MOTION
p
.2
1
g
g
dyne omXlO
O
X
V
bC
T— I
X
£ i
^ 1
*- •&
dyne cm sec .
radian
Ml
O T-i
2X
ST
•ss
1X
m
1
d the centimeter,
dyne second per
g
C
:
§ §
Quantity
Angular
displaceme
Angular
velocity , . .
Torque
Moment of
inertia . . .
Rotational
compliance
Rotational
resistance.
Rotational
reactance. ,
Rotational
impedance
Power
Btrical system
tical, ohm is c
a -3
00
•eo
g
g
S
g
S
g
g
•§§
z&"°
^
S
°
*~
»
**
Ms
•as
o _.
T
,.,
o
-j—
+.
0
0
t^
»-i
g
a *—
^ y
^
o
"3
a
s
l-H
X
X
5'l
Ox
'oo
'oo
s
^0
S
P
0
a
a
a •&
g
•Sx
•gx
*
O_ri
rt
-d
^
a «
a
a
18
s
a
J
;
[
-
* •*—
.-§"
1
I
"3 8
1 «!
il
1
1
Q
1
I
j
M "B,
II
Mechani
resistai
Mechan:
reactan
1 1
%~
i
5-64
ELECTRIC CIRCUITS^ LINES, AND FIELDS
The force equations may be obtained by applying Lagrange's equations to these energy
equations; they are
so <r
m$2 + ~^r — ST£ 4- rmsz = /
Um 4L>
and
Assuming that q can be split into a steady or average part g0 and a varying part qi and
that qi is considerably smaller than g0, so that squares of qi are negligible,
_ _
20' 2C"
The first term on the right-hand side of this equation represents a steady pull or initial
set of the plunger accompanying the initial charge on the condenser. The second term
reduces to — qi, and the third term is negligible by assumption. Neglecting the steady
c/
terms the force equations become
+ rmsz = fz
Qo
'
(19o)
(196)
U.fc \s O
which for steady-state sine waves may be written in the familiar mesh equation form
FZ = 222*2 4" 2i2/l (20a)
El = 2i252 4- 2n/l (206)
where mesh 2 represents the mechanical and mesh 1 the electrical system, zu and 222
are the usual mechanical and electrical impedances and Fz and EI the respective "forces."
z12 = — qo/juC' = ~ l/7*cdCi2 is the interaction factor. The dimensions of I/ CM are such
that multiplication of it by a charge gives a quantity with the dimensions of a force,
while multiplication of it by a distance or length produces a quantity with the dimensions
of an electromotive force.* It is energy divided by distance and charge, and its use
is valid for any system of electrical units in combination with any system of mechanical
units provided those units were used in evaluating ZM.
Equations (20) are then in proper form to use for any case of mechanical and electrical
systems where the interaction between the two systems depends on varying the capacitance
of the electrical circuit by the motion of a part of the mechanical system.
ELECTROMECHANICAL SYSTEMS, MAGNETICALLY COUPLED. When the
interaction between the electric and mechanical systems occurs through magnetic attrac-
FIG. 6. Electromechanical System, Electromagnetically Coupled
tion the inductance of the electric circuit is varied by the mechanical motion. The energy
equations for the system of Fig. 6 are (s0 is the equilibrium position)
and
V = ~
T = —c
D = rmJ22 4-
L
* The factor l/Ci2 has the dimensions of an electric field, although it is a rather unusual expression
for such a field.
ELECTROMECHANICAL-ACOUSTIC SYSTEMS
5-65
Here L, the self-inductance of the electric circuit, is a function of the displacement s^.
Since most of the reluctance of the magnetic circuit is in the air gap rather than in the
iron portions, L can be assumed to vary as the first power of s for small displacements, with
little error. Hence
L = L0(l + 6s2)
where b is a constant depending on the configuration of the physical system and on the
systems of units used.
Applying Lagrange's equations, the force equations for the system are
+ eT
sz - f
and
L --
Assuming that i is composed of a steady, or average, value ZQ and a varying part ii, and
that i\ is considerably smaller than t"0, so that squares of i\ are negligible,
The first term on the right-hand side again represents a steady pull or initial set of the
plunger accompanying the average or d-c exciting current of the magnet. The second
term reduces to — (&Loio)ii, and the third term is negligible by assumption. Disregarding
the steady terms the force equations become
and
which for steady-state sine waves may be written
EI = zuli + zi2S2
(2 la)
(216)
(22a)
^2 = Zn.Ii + Z22S2 = — 212/1 + Z22$2 (226)
where mesh 1 represents the electrical and mesh 2 the mechanical system, EI and F%
represent the respective "forces." In this case, however, the interaction factors are not
equal, but 212 = — 221.
The solutions for current and velocity give
/ _
and
indicating that, when a mechanical force is applied to the plunger in phase with an applied
electromotive force, the velocity of the plunger is increased but the electric current is
decreased. Analysis of the physical action also indicates
this result since increase in the electromotive force attracts
the plunger, but the inward motion of the plunger due to an
applied force increases the inductance of the electric circuit
and so decreases the current flow.
These are the equations of a simple moving-armature
telephone receiver such as that shown in Fig. 7, when eddy
currents are neglected. The input impedance (zt-) of the
receiver is the ratio of EI to /i, when there is no externally
applied force (that is, when F% = 0) , hence p
_ ,
— Zn -f
FIG. 7. Simple Telephone Re-
ceiver (No Eddy Currents)
The blocked impedance of a receiver is defined as the impedance measured when the
diaphragm is constrained from moving (diaphragm held at s = 0) . The motional imped-
ance is the difference between Zi and the damped impedance; that is, it is that part of z*
due to the motion of the diaphragm. Evidently for the simple receiver the damped im-
5-66 ELECTRIC CIRCUITS, LINES, AND FIELDS
pedance is z\\ (which is the impedance of the electric circuit considered alone) and the
motional impedance 2mot. is
2mot. = — (23)
222
Since zia is a constant, independent of frequency by definition, it follows that, if the real
part of Zmot. (the resistance component of zmot.) and corresponding values of the imaginary
component (reactance component) be plotted for various frequencies, the resulting graph
will be a circle, called the motional impedance circle, tangent to the j axis, with center on
the positive real axis (see High-frequency Alternating Currents, Mcllwain and Brainerd,
John Wiley & Sons, Chapter XIII).
MECHANICAL-ACOUSTIC SYSTEM. The simplest mechanical-fluid system is that
where a plunger moves in a fluid displacing a volume of the fluid (see Fig. 8) .
^^^^^^^^^_^ The potential energy of a volume of fluid
^ t%#£#%^^ moving as a unit is
%? "jvtf
ffl ^"m. '^R$| , lUf .
Eluid Tf = l/zplSsP = — - S2
>., Qp mf where p is the density, I the length, S the
^^ cross-section, and m/ the mass of the fluid, and
,
FIG. 8. Simple Mechanical-acoustic System s is the particle velocity. If the fluid is in-
compressible, s for the fluid will equal I, the
velocity of the plunger, and mf will be the actual mass of the fluid; if the fluid is compressi-
ble I may still be taken as the velocity of the plunger but the generalized mass of the fluid
will be less than the actual mass. The potential energy and dissipation are
and
Df = r/
The total energy equations of the system are
2Cf
^ J
-
and
D = rms? + r/s2
where r/ and C/ as well as m/ are generalized parameters. Operating with Lagrange's
equation there results
T- + -r) * + (mm + m/)s + (rm + r/)i (24)
Thus this combination of a mechanical and an acoustic system can be represented by one
equation with only one coordinate, instead of the two equations which might have been
expected. Each parameter of the mechanical system has been altered by the presence
of the acoustic chamber, and the resonance frequency has been lowered.
Assuming sine-wave excitation, eq. (24) becomes
Fm - Ff = \ (rm + rf) + j (wmm + umf - — -- *>Cf J I
or
Fm ~ Ff = ZmfS
where
and
umm + com/
8mf = tan-'
— -
CfC
The net result of the air chamber is thus to increase the resistance and inertial effect
of the plunger but to decrease its compliance. In general both the magnitude and phase
angle of the impedance are altered.
BIBLIOGRAPHY 5-67
BIBLIOGRAPHY
Mcllwain, K., and J. G. Brainerd, High-frequency Alternating Currents. John Wiley (1939).
Olson, H. P., and F. Massa, Applied Acoustics. Blakiston (1934).
_ (1927).
L (1928).
i Nostrand (1942).
Articles
Wegal, R. L., Theory of Telephone Receivers, J. AJ.E.E., Vol. 40, 791 (October 1921).
Hussey, L. W., and L. R. Wrathall, Oscillations in an Electromechanical System, B.S.T.J., VoL 15,
441 (July 1936).
Mason, W. P., and R. A. Sykes, Electrical Wave Filters Employing Crystals with Normal and Divided
Electrodes, B.S.T.J., Vol. 19 (April 1940).
Mason, W. P., Electrical and Mechanical Analogies, B.S.T.J., Vol. 20, 405 (October 1941).
SECTION 6
PASSIVE CIRCUIT ELEMENTS
SINGLE-MESH AND COUPLED CIRCUITS
BY VEKNON D. LAND ON AND
ART. K*0* MdLWAIN pAQE
1. Series Resonant Circuits 02
2. Parallel Resonant Circuits 04
3. Attenuators, Pads 05
4. Coupled Circuits 06
5. Currents and Voltages in Coupled Cir-
cuits 07
6. Air-core Transformers 10
7. Three-winding Transformers (Hybrid
Coils) 12
TRANSFORMERS WITH IRON CORES
BT A. J. ROHNER
8. Audio-frequency Transformers 13
9. Output Transformers 17
10. Input and Interstage Transformers 19
11. Driver Transformer 22
12. Physical Design of Audio Transformers 22
13. Audio Transformer Measurements 25
14. Power Transformer 26
15. Vibrator Transformer 30
16. Pulse Transformer 32
ELECTRIC WAVE FILTERS
^•r, BT A. J. GHOSSMAN PAGE
17. Introduction 33
18. Properties of the Image Parameters. ... 36
19. Open-circuit Transfer Impedance 38
20. Transfer Constant Theorem 39
21. Image Impedance Theorem 39
22. The General Composite Filter 40
23. Symmetrical Sections 41
24. Unsymmetrical Sections 50
25. Tchebycheff Type Characteristics 56
26. Mayer's Theorem 61
RADIO ANTENNAS
BT J. C. SCHELLENG
27. Principles of Linear Conductor Antennas 65
28. Principles of Directivity 71
29. Directivity of Linear Conductor An-
tennas 73
30. Directivity of Quasi-optical Antennas
and Horns 76
31. Practical Antenna Systems 80
32. Direction Finding 87
33. Miscellaneous 88
6-01
PASSIVE CIRCUIT ELEMENTS
SINGLE-MESH AND COUPLED CIRCUITS
By Vernon D. Landon and Knox Mcllwain
The individual elements used in communication circuits must be carefully designed to
meet certain definite specifications if the circuit as a whole is to function properly. Among
the more important factors to be considered are the efficiency and load-carrying capacity
of the element, its impedance, its selectivity, and the introduction of the various forms of
distortion.
Circuit requirements frequently demand not only that the transmission (ratio of output
to input) have a particular value at a given frequency, but also that the variation of
transmission with frequency, called the transmission-frequency characteristic, have a
definite form.
1. SERIES RESONANT CIRCUITS
Figure 1 represents a series circuit in which the resistance of all the elements of the cir-
cuit is lumped into one resistance r, and similarly for the inductance and capacitance. For
a given value of impressed voltage the current in this circuit depends on r, L, and C, and
the frequency of the impressed voltage. For given
values of L and C there will be one frequency, and
only one, for which coL = 1/coC. At this frequency
(fr}, which is called the resonant frequency of the
circuit, the current is maximum for any given value
of voltage and is in phase with the impressed volt-
age. The resonant frequency is given by
FIG. 1. Simple Series Resonant Circuit
fr-
(1)
where L is in henrys and C in farads. When L is expressed in millihenry s and C in micro-
farads eq. (1) becomes:
5033 ., .
'' " VTc (U)
The absolute value of the current Ir in the circuit at this frequency is
(2)
For frequencies less than fr, coL < — — ; and the current will lead the impressed voltage
(/3 is negative), whereas for frequencies greater than fr the current will lag the voltage
(j3 is positive, see Section 5, article 2) .
In Fig. 2 are shown graphs of the absolute values of current versus frequency in a
simple series circuit for two values of resistance.
VOLTAGE RELATIONS. At the resonant frequency the magnitude of the impressed
voltage is given by E = rl, and the voltages across the inductor and condenser are
2irfrLI and Ec — 0_r^ . Since the only condition necessary for resonance is that
the sum of the reactances is zero, either reactance may be many times as great as the
circuit resistance; thus the voltage across the inductor, or the condenser, may be several
hundred times the impressed voltage. Figure 3 shows how the voltage components in a
circuit vary as the frequency is changed.
6-02
SERIES RESONANT CIRCUITS
6-03
24
22
20
18
£16
a
Jl4
k
J>12
"c
£
3 10
8
6
4
2
0
\
1
L~
655 Mh.
0.0605 Mf.
60 Ohms
1060 Ohms
1.3 Volts
rz-
?*•—
E=
J
L-i
i
1^
\
5
o-?
J
\
,E
- =
Q.
<
V
p
-**&*
•-"*""
i?>
-^>
f*-^
400 500 600 700 800 1000 1200 1400 1600
Frequency^ Cycles per Second
2<X
FIG. 2. Variation of Current with Frequency in a Simple Series Circuit (Ji is for resistance n, and
/2 for rs)
400
500
600 700 800 1000
Frequency in Cycles per Second
1200 1400 1600
2000
FIG. 3. Variation of Voltage Components with Frequency in a Simple Series Circuit
6-04
PASSIVE CIRCUIT ELEMENTS
CIRCUIT Q. The per cent change in current from its maximum value for a given
percentage frequency change depends on the relative values of r, L, and C. As a measure
of this change a factor Q is defined as oxL/r.
From this the voltage across the coil (or
condenser) of a simple series circuit at re-
0.7
3 0.6
; 0.4
'0.3
7
\/
60
40
20
-40
-60
-80
-2.0 -1.5 -1.0 -0.5 0 0.5
Value of a
1.0 1.5 2.0
FIG. 4. Values of a Universal Resonance Curve.
Calculated from
1+ ~ + 3 a
sonance is
2irfrLE
= EQ
(3)
For a given value of inductance the circuit
having the higher Q will have smaller r, will
have higher resonance current in compari-
son to current off resonance, will be repre-
sented by a more sharply peaked current
vs. frequency curve, and is said to be more
sharply tuned.
Universal Resonance Curve. Terman
has shown that, when Q is constant (loss
resistance proportional to frequency), the
relation of resonant current to current off
resonance for any circuit can be plotted in a
universal resonance curve as shown in Fig. 4.
If the ratio of the actual current and the
current at resonance are known, the ordi-
nate is established and therefore the two
possible values of a. From these the re-
quired deviation in frequency is determined
from the relation
- Q
Cycles off resonance
Resonant frequency
(4)
Conversely, if the deviation in frequency is
since a/Q is quite small. For paraUel circuits ^nversely, it the deviation in frequency is
change ratio of currents to ratios of impedances •lmown> a can be readily found and thence
ft,r\f{ Ifo.Hl'nO1 'nhn.SR fl.nfrlps f.n laororincr +.ll» Vola+.-lTrii Tac-r\r\r\ DQ
o mp
and leading phase angles to lagging.
•>
the relative response.
2. PARALLEL RESONANT CIRCUITS
It is not so easy to define resonance in a parallel circuit. If the condition xi = wL =
- xz = l/o>C is used, there results
and
n-hs
(5)
x = ri +r2 Xl (6)
so that as n and rz decrease r rises indefinitely and theoretically becomes infinite when
the circuit resistance is zero. However, x is not zero at the fre-
quency/,., so that the current is not in phase with the voltage, nor
is s a maximum. Either of these last conditions may be the
important one, and the condition of z maximum (I minimum) is
certainly the easiest to measure. If n — ro the three conditions
coincide, and are but slightly different when n and rz are small.
In the particular important case of a coil and condenser in
parallel (Fig. 5) these equations reduce (neglecting the resistance
of the condenser) to
FIG. 5. Simple Parallel
Resonant Circuit
r = — - and
rLC
and the frequency for which x = 0 is
(£-•
(7)
(8)
Graphs of r, x, and Z for such a circuit are shown in Fig. 6.
ATTENUATORS, PADS
6-05
200,000
160,000
£120,000
2 80,000
40,000 -
700 800 900
Frequency in Cycles per Second
1100 1200
•f 60,000
+40,000
-h 20,000
-20,000
-40,000
—60.000
FIG. 6. Variation of the Impedance of a Simple Parallel Circuit with Frequency
Another case of particular interest exists when TL — TC = VL/C. Then for any
frequency
r - VL/C = TL = re and x = 0 (9)
Thus the apparent resistance is constant with frequency, and the apparent reactance is
zero for all frequencies.
TUNING. Although they are subject to the same limitations as regards controlling
selectivity and frequency characteristic as the series resonant meshes, simple parallel
tuned circuits are frequently used as coupling elements between vacuum tubes. When
the circuit of Fig. 5 is adjusted for unity power factor, Ie = EXL/(T* + XLZ), IL =
.E/Vr2 + XLZ, Iz — ErC/L, and z = L/rC. If the capacitance only is varied, unity power
factor coincides with the condition of Tnii-iin-mm line current and with maximum impedance.
When the circuit is tuned by adjustment of the inductance this is not true, and in this
case full output is obtained for a slight detuning from the condition of minimum plate
current. If the resistance remains constant the maximum impedance is
where
XL = r
- 1
whereas if the phase angle (XL/T) of the inductance remains constant the maximum im-
pedance is z = vr2 -+- #L2 XL/T which occurs when XL = xc-
(For further details see R,. Lee, Proc. I.R.E., Vol. 21, 271.)
3. ATTENUATORS, PADS
Use of the concepts and equations of insertion loss (Section 5, article 7) permits the
designs of definite elements (either dipoles or quadripoles) which may be inserted into
circuits to produce definite effects at a given frequency. Such elements are called attenu-
ator sections, or sometimes pads; more complicated sections which aim to provide a desired
definite variation of loss with frequency are termed distortion correctors, or equalizers.
6-06
PASSIVE CIRCUIT ELEMENTS
MATCHED IMPEDANCES. The simplest design occurs when it is desirable to have-
uniform loss at all frequencies, in which case the image impedances of the network must
match those of the circuit into which it is inserted. By Thevenin's theorem (p. 5-12) the
circuit, no matter how complicated, can be reduced to a generator in series with a simple
impedance on each side of the point of insertion. (See Figs. 7 and 8.)
These impedances are designated by Z and z and their ratio by Z/z = s2. Either T or
TT type sections may be utilized. The formulas are most useful for resistive networks.
FIG. 7. T Section Attenuator
T SECTIONS. To design a T section (see Fig. 7) which causes a loss of n decibels, read
off the current ratio (k) corresponding to such a loss in the decibel table, Section 1. Then
the proper values for the arms of the T section are
- 2k/ s
I + k* - 2ks\
i-g r and
k
When the impedances in either direction are equal,
1 - k
1 — z, then s = 1 and u = v ••
1 + k
z and w
2k
For instance, to cause a loss of 3 db in a circuit where Z = z = 500 / 60°, k = 0.7080,
u = v = 85.5 Z60°, and w = 1420 Z60°.
To design a balanced T or H section simply put */2 u and 1/2 v in each series leg.
TT SECTIONS. The proper values for the arms of the TT section of Fig. 8 are
- A?
sz _
' and
- kz
When the impedances in either direction are equal, Z = z, then s = 1 and u ~ w
FIG. 8. v Section Attenuator
Tabular aids in computing such sections and rules for other types of sections are given,
by McElroy (Proc. I.R.E., Vol. 23, 213 [March 1935]).
NON-MATCHED IMPEDANCES. When the impedance variation with frequency
of the terminating circuits is such that it cannot be duplicated in a simple network, the
insertion loss of the network at any frequency can be obtained by the methods of Section
5, article 8. Exact methods of design of sections to insure a predetermined variation of
loss (and phase change) with frequency are given by Mead (B.S.T.J., Vol. 7, 195),
Zobel (B.S.T.J., Vol. 7, 438) and Gewertz (Network Synthesis, Williams and Wilkins
Co. [1933]).
4. COUPLED CIRCUITS
Two electric meshes are said to be coupled to each other when they have an impedance
in common, so that a current in one causes a voltage in the other. The common, or
mutual, impedance is defined as the factor by which the current in one mesh must be
CURKENTS AND VOLTAGES IN COUPLED CIRCUITS 6-07
multiplied to give the voltage, due to that current, in the second mesh. It may be a pure
resistance, or a pure reactance, in which case the meshes are said to have a pure coupling-
or the common impedance may be complex, in which case the coupling is said to be complex
Figures 9 and 10 illustrate some of the more usual types of coupling, although a com-
plicated intervening network may be considered as simply a coupling impedance if the
relation between current in one mesh and resulting voltage in the other is of interest
Mesh a < Mesh 6 Mesh a § Mesh 6
A. Resistance Coupling B. Inductance Coupling
Mesh
Mesh 6
C. Mutual Inductance
Coupling
D. Capacitance Coupfing
FIG. 9. Simple Types of Coupling
MUTUAL IMPEDANCES. The mutual impedances of the circuits shown in Fig. 9
are ZM = r, juL, jcoM, 1/jcaC. In Fig. 10, case E, the mutual impedance is ju(L' + Jlf)
if the windings are in the same sense and jut(L' — M) if they are in opposite sense. In
case F, ZM = jfaL - 1/coC); in case G, ZM = jfaL/oPLC - 1). When the middle mesh
of case H is considered as a mutual impedance between meshes a and b its value is
when the transformer windings are so connected as to have minimum voltage across the
coupling condenser. Reversing one winding reverses the sign of M .
Mesh 6
& Combined Self and
Mutual Inductance
F. Inductance and
Capacitance Coupling
Mesh GL
Mesh6
G. Parallel Resonant-
Coupling
H. Mutual Inductance and
Capacitance Coupling
FIG. 10. Common Types of Involved Coupling
5. CURRENTS AND VOLTAGES IN COUPLED CIRCUITS
If two meshes are coupled as shown ha Fig. 11 the primary current is
« B/z.'
where
and
— Taa -f- •
(10)
(lOo)
(106)
Note that in these equations TM and r&& are the self-resistances of the respective meshes
(raa = TOO + rm}t and Xaa and XM are the self -reactances. (For a complete discussion of
6-08
PASSIVE CIRCUIT ELEMENTS
self-impedances and mesh currents see Section 5, article 4. zc' is called the equivalent
primary impedance and ra' and xd the equivalent primary resistance and reactance. The
Ll '•
1
f I» }
FIG. 11. Two Meshes Coupled through an Impedance zm
.second term on the right of eq. (10a) is called the transferred resistance, and the correspond-
ing term of eq. (106) the transferred reactance.
The secondary current is
I& = Zmla/Zbb = ZmE/ZoaZ&' (11)
where
/ , Xm Faa Tm ^aa ^>fmXmXaa /-, -. \
TV = ?bb H o (Ha)
and
xbr
— XmXaa ~
RESISTANCE COUPLING. When the coupling is a pure resistance, eqs. (lla and 6)
reduce to
Tb = rbb - rtr
and
Xb = ^66 + T
so that the secondary current is
and its absolute value is
J6«
r ****** _L Y _L r^^\ i
Zoo r&& =- + ; I Xbb H S~ )
L Zao2 \ 2oa^ /J
(13)
w2roa\2
(13o)
;66 = 0) is
(14)
REACTANCE COUPLING. When the coupling is a pure reactance, eqs. (lla and 6)
reduce to
The maximum value possible for Ib (for optimum tuning arrangements, xa
T
-i & max max :
and
Xb = Xbb ~~ Xfn Xaa/ Zaa,
so that the expression for the secondary current becomes
, jxmE
zoc
and its absolute value is
xm*rai
zaa2
./ Xm2Xaa\l
3(Xbb-^^~)\
(156)
(16)
(16a)
Since the nature of the curve of secondary current against mesh reactances (Fig. 12)
changes completely at the point where xmz — raafbb this condition is defined as the con-
dition of critical coupling. The condition when xm2 > raarbb is spoken of as coupling
greater than critical, whereas when xmz < raor&& the coupling is said to be less than critical.
CURRENTS AND VOLTAGES IN COUPLED CIRCUITS 6-09
0 oca -H
FIG. 12. Variation of J& max with Primary Reactance for Three Degrees of Coupling
These conditions have been variously named adequate and inadequate coupling, sufficient
and deficient coupling, super and sub coupling; there is no general agreement as to termi-
nology.
When the coupling is less than or equal to critical there is only one inflection point on the
curve of /& max against primary reactance, which gives a maximum value for xa — #& = 0,
or when each mesh is separately tuned to resonance. When the coupling is greater than
critical the current curve shows a Tnim'Trm™ for the condition xa = x& = 0 with maximum
points on either side of zero. The proper adjustments and absolute value of currents
obtainable are shown in Table 1.
Table 1.
Conditions for and Values of Maximum Secondaty Current in Two
Mesh Circuits (For Best Possible Tuning)
Reactance Coupling
Resistance
Coupling
zm2 <raan&
Xm* = TaaTbb
Xmz >Taarvb
Opti'mTl'm Yftlm^ for Xa - - * •
0
0
0
•\J~(xm2-raar6&)
Optimum value for Xh - - -
0
0
0
\l™ (xm* - Taar&ft)
*Taa
Maximum secondary current
Exm
E
E
Erm
raarbb 4- £m2
2Vraarbb
2Vr£MrZ)6
Toanjb - Trr?
Corresponding primary cur-
cent . . ........
Erw
E
E
Eru>
TooTM + Xm*
2r<w
2TcKj
roan* ~ rm*
Coupled circuits are frequently used to match two circuits with dissimilar impedances.
The conditions listed in Table 1 for maximum secondary current also give the conditions
for maximum power transfer and so for conjugate impedances.
TRANSMISSION-FREQUENCY CHARACTERISTIC. The most-used form of cou-
pled circuit is that of Fig. 10, case H. Assuming that the distributed capacitance between
windings is negligible, the transmission formula is
H- IP - (1 -
(17)
where K = M/^/LiLz is called the coefficient of coupling, and di and d* are the decrement
coefficients at resonance of the two meshes. Near resonance where F = 1 approximately
r- v==
/r)//r]2
(18)
The shape of the transmission curve as the frequency varies depends on the coefficients
(di* -f- d£ — 2K?) and (didz + K^. With three independent variables resulting in two
coefficients there are many solutions for a given shape. For a maximum transmission
the additional condition may be specified that K is as large as possible.
6-10
PASSIVE CIRCUIT ELEMENTS
SELECTIVITY. Comparing eq. (18) with eq. (4) for a single circuit it is seen that for
frequencies some distance from resonance the transmission for a coupled circuit varies
roughly inversely as the square of the departure from resonance, while for the single
circuit the variation is roughly as the inverse first power. The transmission of two single
circuits in cascade (and separated by a vacuum tube) is the product of the separate trans-
missions. For two circuits of decrement coefficients di and dz this would be
V[2</ -
- /r)//rP
(19)
Comparison of this with eq. (18) shows that the selectivity of the coupled circuit approaches
that of the cascaded single circuits as K decreases, but the transmission of the coupled
circuit is decreased in the process.
(For complete discussion see Puring-
ton, Proc. I.R.E., Vol. 18, 983 [June
1930], and Aiken, Proc. LR.E., Vol.
25, 230 [February 1937].) Figure 13
shows the selectivity to be expected
with well-designed coupled circuits.
Curve C is for critical coupling;
curve D for greater than critical
coupling; and curves A and B for
less than critical coupling.
STAGGERED TUNING. The
selectivity curve of a pair of coupled
resonant circuits may be duplicated
by the use of a two-stage amplifier
having a single tuned circuit per
stage, one circuit being tuned above
and the other below the desired
mean frequency. Similarly any de-
sired number of single-tuned-circuit
stages may be used to obtain an
overall selectivity curve with a flat
top and steep sides. The tuning
points are distributed systematically
across the pass bands. The effective
Q is highest on the circuits tuned
near the cutoff frequency. See Sec-
tion 7, article 13; also the literature
_ _2Q ;- — io Q 10 20
Frequency Removed from Resonance in Kc. Amplifiers
FIG. 13. Selectivity of Coupled Circuits «7, critical cou- RCA Rev., Vol. V, No. 3-4 [January-
pling; D, greater than critical; A and B, less than critical) April 1941]) .
6. AIR-CORE TRANSFORMERS
Since almost all air-core transformers used in communication circuits employ tuned
secondaries only such cases will be considered. A simple circuit for a tuned amplifier
stage is shown in Fig. 14 A. The amplification or gain of such a stage is defined as the
ratio of the voltage applied to the grid of the first tube to the voltage delivered to the grid
of the second tube. The value of the gain at resonance is
Ei
M
(20)
where n is the amplification factor of the tube.
In this equation (jPM*/rs represents the impedance reflected into the primary circuit
by the tuned secondary circuit. It is assumed in this equation that the primary reactance
is negligible.
This equation may be written in a simpler algebraic form but is most easily remembered
and used in the form shown. Keeping in mind that (j^M^/rs is the load on the tube it is
C^M^/TS
evident that uEi . n^^ , N — ; is the voltage drop across the plate load. Multiplying
(u*M*/ra} + rp
this voltage by the ratio of transformation L9/M gives JEfe, the output voltage.
AIR-CORE TRANSFORMERS
6-11
As the mutual reactance between the primary and secondary circuits is varied, a
maximum of gain is obtained when the value of vf&P/rs is equal to rP. This constitutes
matching the impedance of the tube.
In modern tubes of the screen-grid or of the pentode type, the plate impedance (rp) is
of such a high magnitude that it is ordinarily impracticable to match its impedance. In
fact, ordinarily the load in the plate circuit is so small as to have a negligible effect upon
the plate current, in which case the formula" for gain becomes ~ = m ~ , where
EI rs M
sm is the mutual conductance, or transconductance, of the tube. Expressing this equation
in words, the gain of a tuned amplifier, employing a tube of very high plate impedance,
is equal to the transconductance, multiplied by the load impedance, and by the trans-
formation ratio.
The equation may be written in another form, — = s,
t — wJK".
That is, the gain
is equal to the transconductance, divided by the power factor of the secondary, and
multiplied by the mutual reactance.
FIG. 14. Tuned Amplifier Circuits
VARIATION OF GAIN WITH FREQUENCY OF RESONANCE. The gain of an
amplifier of this type varies considerably with frequency as it is tuned over the frequency
band. The frequency squared occurs in the numerator, causing the gain to tend to be
larger at the high-frequency end of the tuning range. This tendency is partly counter-
balanced by the normal variation of the circuit resistance with frequency. The rate of
change of resistance varies considerably from coil to coil, but the resistance varies faster
than the first power of the frequency, and slower than the second power. If the resistance
varies directly with the frequency the gain is proportional to the frequency of resonance.
However, if the resistance is proportional to the square of the frequency the gain is con-
stant. Usually the resistance rises only slightly faster than the frequency, causing the
gam to rise with frequency.
EFFECT OF LEAKAGE REACTANCE. With tight coupling it is justifiable to neglect
the primary reactance and the tube's plate-filament capacitance, because the value of the
reflected impedance exceeds the primary reactance so greatly.
However, when the coupling is only moderate, the plate-filament capacitance and the
primary reactance are no longer negligible. The effect is to increase the gain, above that
of the formula, especially at high frequencies.
In practice, the transformer is frequently of such a design that the primary reactance
is far from negligible. The gain formula then becomes somewhat too complicated for
practical use. Cut-and-try methods are the rule for designing such transformers.
TUNED R-F TRANSFORMER EMPLOYING COMPOUND COUPLING. A com-
mon design of transformer in broadcast receivers employing screen-grid tubes is that shown
in Fig. 14B. It employs a primary of such a high inductance that its primary is resonant
in conjunction with the output capacitance of the tube, at a frequency below the broadcast
frequency spectrum, 450 kc and below. The secondary coil is of the usual type, but the
per cent coupling is quite low, usually between 15 and 25 per cent. Sufficient capacitance
•coupling is used to give the desired high-frequency gain.
The performance of this transformer is an improvement over that of the low-inductance
primary type, in that the gain may be made more nearly constant throughout the tuning
range.
The average voltage gain in this type of transformer is somewhat less, but the great
amplifying ability of screen-grid tubes makes it unnecessary to obtain the greatest possible
gain in transformers.
6-12
PASSIVE CIRCUIT ELEMENTS
7. THREE-WINDING TRANSFORMERS (HYBRID COILS)
It is frequently desirable in electric circuits that currents in one portion of a circuit
shall induce voltage in all branches of the circuit except certain designated ones, in which
no voltage is to be introduced. This may be accomplished by means of an impedance
bridge (Fig. 15) which consists of six adjustable impedances arranged in the form of a
Wheatstone bridge. If the impedances are so adjusted that for a certain frequency
ZA/ZB = ZC/ZD a voltage of that frequency introduced at E will cause no current in the
arm Or, and vice versa.
FIG. 15. Impedance Bridge Circuit
FIG. 16. Schematic Circuit of Three- winding
Transformer with Load
A more widely used means of blocking voltages out of a particular branch is a combina-
tion of three coils such as that shown in Fig. 16; it is optionally called a three-winding
transformer or a hybrid coil. If the two coils La are wound series aiding and the transformer
is well made so that the winding resistances may be neglected and the coefficients of
coupling are practically unity, then a voltage E\ will cause no current through ^2 (and
vice versa) provided z3 = zJN1*, where TV is the turn ratio between one of the La coils and
the Lb coil. Also if zi = 22 a voltage #3 will cause no current through E±, and vice versa.
If all these conditions are fulfilled, then power from E\ or E<z will divide equally between
73 and z4 and power from E$ and E± will divide equally between zi and zj. Such trans-
formers are extensively used in bidirectional amplifiers (see p. 7-13) ; also this circuit is the
basic circuit for all neutralizing circuits. (See p. 7-29)
BIBLIOGRAPHY
Adams, J. J., Undercoupling in Tuned Coupled Circuits to Realize Optimum Gain and Selectivity..
Proc. I.R.E., Vol. 29, 277 (May 1941).
Aiken, C. B., Two-mesh Tuned Coupled Circuit Filters, Proc. I.R.E., Vol. 25, 230 (February 1937).
Blanchard, J., The History of Electrical Resonance, B.S.T.J., Vol. 20, 415 (October 1941).
Everitt, W. LM Communication Engineering. McGraw-Hill, New York (1937).
Johnson, K S.f Transmission Circuits for Telephonic Communication. Van Nostrand, New York (1925).
King, R., The Application of Low-frequency Circuit Analysis to the Problem of Distributed Coupling
in Ultra-high-frequency Circuits, Proc. I.R.E., Vol. 27, 715 (November 1939).
King, R., A Generalized Coupling Theorem for Ultra-high-frequency Circuits, Proc. I.R.E., Vol. 28,.
84 (February 1940).
Korman, N. I., Coupled Resonant Circuits for Transmitters, Proc. I.R.E., Vol. 31, 28 (January 1943).
Landon, V. D., Cascade Amplifiers with Maximal Flatness, R.C.A. Review, Vol. 5, No. 3-4 (January
1941).
Lee, R,, A Practical Analysis of Parallel Resonance, Proc. I.R.E., Vol. 21, 271 (February 1933).
McElroy, P. K., Designing Resistive Attenuating Networks, Proc. I.R.E., Vol. 23, 213 (March 1935).
Mcllwain, K., and J. G. Brainerd, High-frequency Alternating Currents. John Wiley, New York (1939).
Mead, S. P., Phase Distortion and Phase Distortion Correction, B.S.T.J., Vol. 7, 195 (April 1928).
Nelson, J. R., A Theoretical Comparison of Coupled Amplifiers with Staggered Circuits, Proc. I.R.E.?
Vol. 20, 1203 (July 1932).
Purington, E. S., Single- and Coupled-circuit Systems, Proc. I.R.E., Vol. 18, 983 (June 1930).
Sherman, J. B., Some Aspects of Coupled and Resonant Circuits, Proc. I.R.E., Vol. 30, 505 (November
1942).
Terman, F. E., Radio Engineering. McGraw-Hill, New York (1937).
Zobel, 0. J., Distortion Correction in Electrical Circuits, B.S.T.J., Vol. 7, 438 (July 1928).
Also many articles in Proc. I.R.E., J. A.I.E.E., and Experimental Wireless and Wireless Eng.
AUDIO-FREQUENCY TRANSFORMERS 6-13
TRANSFORMERS WITH IRON CORES
By A. J. Rohner
8. AUDIO-FREQUENCY TRANSFORMERS
The Function of the audio-frequency transformer is to couple various circuits, at audio
frequencies, over a considerable range of the audio-frequency band. It may be used as
an impedance-matching device, as a means of isolating circuits, or as a means of obtaining
phase reversal. "When it couples a voltage source, such as a microphone, a phonograph
pick-up, or a telephone line, to the grid of a vacuum tube, it is usually called an input
transformer. If it couples the plate of one tube to the grid of another, it is called an
interstage transformer. If it couples the plate of a vacuum tube to some sort of load,
such as a loudspeaker, indicating meter, or telephone line, it is referred to as an output
transformer. The modulation transformer is a special case of the output transformer, in
which the load is the plate of a radio-frequency amplifier tube. If the transformer is used
to match telephone lines of unequal impedance, or to isolate lines of equal impedance,
it is called a line transformer. There are, of course, many variations of the above-men-
tioned applications.
The audio-frequency transformer is constructed much like a power transformer, but
there are two distinct points of difference. Power transformers are usually one-frequency
devices, whereas audio transformers must operate over a wide band of frequencies. In
high-fidelity systems, for example, a range of from 30 to 15,000 cycles may be required.
In systems where intelligibility of speech is all that is necessary, 300 to 3000 cycles may
suffice. Then, too, the power transformer works from a voltage source having good regula-
tion; that is, the impedance of the source, or "generator impedance," is negligible as com-
pared with the load impedance. An audio transformer always works from a voltage source
having poor regulation, the generator impedance often being equal to the load impedance,
and in pentode or Class B power amplifiers, being greater than the load impedance.
These two factors, wide frequency range, and high generator impedance, place severe
restrictions on the constants of an audio transformer. Primary inductance must be high;
leakage inductance and distributed and other ca-
pacitances must be low. See G. Koehler, Design of
Transformers for Audio-frequency Amplifiers with
Preassigned Characteristics, Proc* LR.E. (December
1928); P. W. Willans, Low-frequency Intervalve
Transformers, LE.E. J. (October 1926).
COUPLED CIRCUITS. The design of an audio-
frequency transformer requires the solution of
coupled circuits, of which the transformer is a part,
and including the generator and the load imped- FICL i. Fundamental Circuit
ances. This solution may be carried out by the
classical method, using mutual inductance. See article 4, Coupled Circuits. Thus, for
the circuit of Fig. 1, the voltage impressed on the primary is
CD
TL -r J^^a
The impedance "looking in" to the primary is
.SH/rt,
(2)
The voltage across the load, TL, is
Et = rzJ2 = TV*, (3)
This method becomes quite complicated, however, when all the factors affecting audio
transformers are considered: core loss, winding resistances, distributed capacitance, inter-
winding capacitance, turns ratio, etc. The first step in simplifying the analysis of the
audio transformer and its associated circuits is to convert them to an equivalent direct-
connected network. See J. H. Moreeroft, Principles of Radio Communication, 2nd Ed.,
pp. 95-105.
EQUIVALENT DIRECT-CONNECTED NETWORK. Considering the transformer
shown in Fig. 1 as a unity-ratio transformer, LI — £2. Then kLi = kL$, where k »
coefficient of coupling, and M = fcVZiLa — kLi, where M is the mutual inductance.
6-14
PASSIVE CIRCUIT ELEMENTS
The leakage inductance of the primary, or that portion of the primary which is not
coupled to the secondary, equals (1 — &)Z/i, Similarly, the portion of the secondary not
coupled to the primary equals (1 — fc)La» which is, of course, equal to (1 — k)Li. The
circuit of Fig. 1 can now be replaced by a direct-connected network as shown by Fig. 2.
The common impedance is kLi.
It may be shown that this circuit is the exact equivalent of Fig. 1. For example, the
input impedance equals Z\ and
Substituting M for kLi, and 1/2 for LI
TL 4- jwLi
to'Jif8
?"L + juLiz
which is the expression derived for the circuit of Fig. 1.
The equivalent network of an inequality ratio transformer may be referred to either
the primary or secondary circuit, provided the correct transformations are made. To reflect
. n the secondary constants to the primary,
P u-AOLi. U-*;L2 for example? it is necessary to multiply
all the impedances on the secondary side
by the ratio Li/Z/2- With iron-core trans-
formers, the ratio 1/1/1/2 is for all practical
purposes equal to the square of the turns
ratio. Voltages are transformed by the
turns ratio, currents by the inverse of the
turns ratio,
secondary turns, the secondary constants, referred
FIG. 2. Equivalent Network
If Np = primary turns, and N8 =
to the primary, are
After these conversions are made, the transformer becomes a unity-ratio transformer
and can. be replaced by an equivalent direct-connected network.
COMPLETE EQUIVALENT NETWORK. Figure 3 shows the complete equivalent
network of an audio-frequency transformer, referred to the primary, in which EI is the
generator voltage (pEg in the case of a vacuum tube); rp is the generator resistance;
Ci is the distributed capacitance of the primary winding, plus any additional capacitance
across that winding; TI is the primary winding resistance; rc is the core-loss resistance; r-^f
is the secondary winding resistance,
referred to the primary; C2' is the . TP .ri <l-fc>Li
distributed capacitance of the sec-
ondary winding, plus additional
capacitances across that winding
within the transformer itself, re-
ferred to the primary; and rz,', Ci/,
and JSV are the load resistance, load
capacitance, and load voltage, all
referred to the primary.
FIG. 3. Equivalent Network of Audio Transformer
The "additional capacitances" spoken of may be capacitances of the windings to ground,
or capacitance between windings. For example, a single-ended interstage transformer
might have its primary on the inside, next to the core, and secondary on the outside,
wound over the primary. If the primary finish is connected to +B, and the secondary
start is connected to ground, there is no a-c potential between the adj acent surfaces of the
two windings, so that capacitance between the two windings has no effect. However, the
primary start would go to plate, and the start layer of the winding has capacitance to the
core. This capacitance is an additional capacitance across the primary winding. Simi-
larly, the secondary finish would go to grid, and any capacitance existing between the
finish layer of the secondary and the core or case would be an additional capacitance across
the secondary winding. If the connections to both windings were reversed, making primary
start +J5, and secondary finish ground, those capacitances would have no effect. The
capacitance between windings, however, would be of great importance. This would be
somewhat equivalent to an additional capacitance across the winding having the most
turns. Use of a grounded electrostatic shield between windings will largely eliminate
AUDIO-FREQUENCY TRANSFORMERS
6-15
capacitance between windings, but, of course, it adds additional capacitances to
ground.
Solution of the circuit of Fig. 3 will give the characteristics of the audio transformer,
such as (1) voltage ratio as a function of frequency; (2) primary impedance as a function
of frequency; (3) phase shift as a function of frequency; (4) efficiency.
SIMPLIFIED NETWORK AT LOW FREQUENCIES. The network of Fig. 3 can be
greatly simplified for practical design purposes by considering, first, the effect of frequencj^
upon the relative importance of the various constants, and second, the particular applica-
tion in which the transformer is used.
At low frequencies, leakage inductance
and all the capacitances can be ignored.
Furthermore the coefficient of coupling, k,
of most audio transformers is above 0.995,
so that kLi may be taken as LI with an
error of less than 1 per cent. The low-
frequency characteristics of any audio
transformer are determined by the pri-
mary inductance and the various resist-
ances of the network, as shown in Fig. 4.
But Fig. 4 can be simplified still further,
single resistor, as shown in Figs. 5 and 6.
FIG. 4. Network at Low Frequencies
The resistances can be lumped together into a
Let ra = rp + r\ and let r& = rj -f ^i/- Then
the lumped resistance, R, is equivalent to ra, r&, and re in parallel, or
R =
(4)
If the input voltage, EI, is multiplied by the attenuation of the resistance network, the
circuit of Fig. 5 becomes identical, in its output voltage and phase shift, with Fig. 4.
The new value for the input voltage, of Fig. 5, is
E =
(5)
4- Tofc + TbTc
Figure 6 is simply a redrawing of Fig. 5, showing the single resistor and the new input
voltage. Figure 6 is an exact equivalent of Fig. 4 as far as voltage output and phase
Eix rarb+rarc+rbrc
FIG. 5. Method of Combining Resistances
FIG. 6. Circuit of Audio Trans-
former at Low Frequencies
shift are concerned. The voltage output and the phase shift, at low frequencies, of all
audio transformers are given by this simple circuit. Figure 7 shows those characteristics,
as a function of 27rfLi/R.
At some frequency, 2irfLi = Rt so that 2irfLi/R = 1- Let this particular frequency be
called /i. This is the low frequency at which the response has dropped 3 db from its value
in the middle-frequency range. At twice this frequency, 2ir/Li/R = 2. At three times
this frequency, 2irfLi/R = 3, etc. At any frequency, /, 2irfLi/R = f/J\. The curves
given in Fig. V, as a function of 2irfLi/R, are at the same time frequency characteristics,
the frequency being expressed in terms of the reference frequency, f\.
In order to determine the proper value of primary inductance, it is necessary to know
what drop in secondary voltage is permissible, at some specified low frequency, as com-
pared with the voltage in the middle-frequency range. For example, 1-db drop at 100
cycles might be given as the requirement of low-frequency response. From Fig. 7, the
ratio of 2irfLi/R is found, which gives this particular drop. As a first approximation, the
winding and core-loss resistances may be neglected, so
(6)
(7)
" — Tv + rL'
Then
i2^ x —
12 27T/
6-K
1.0
.9
.8
f .7
3
o .6
CO
bo
|.5
^>
to q
3 PASSIVE CIRCUIT ELEMENTS
=
0
10
20 g
30 I
40 |
50^
CO
60 £
CO
70S
sol
90
100
^-~'
— —
_
i-
^^
^
.^ — -
o—
/ ^
^
co 4-
f\
/
^
3 5-
<,
^
z
jf
m 6
Q -
/
X
X
$
'<?-
10-
X
^
^.a
.1
0
12-
^
•^
•^pi
^
1 .2 .4 .6 .8 1 2 4 6 8 10
Ratio Primary Reactance/Resistance=2^/lD1/K. or Frequency Ratio—///!
FIG. 7. Response and Phase Shift at Low Frequencies
SIMPLIFIED NETWORK AT MIDDLE FREQUENCIES. In this frequency range,
all reactance elements become negligible, and the transformer reduces to a network of
resistances, as shown in Fig. 8. In this range, phase shift is practically zero. This is the
"flat" portion of the frequency-response characteristic, the secondary voltage being
- N* v
77~ X
v
X
TL'Te
;
-f- rarc
and the efficiency of the transformer being, to a very close approximation,
Efficiency =
rL'
2r2'
(8)
(9)
SIMPLIFIED NETWORK AT HIGH FREQUENCIES. The shunting effect of the
primary inductance is negligible at high frequencies. See Fig. 7. If the generator resist-
ance, rp, or the reflected load resistance, r^/, is
less than 20,000 ohms, the primary capaci-
tance, Ci, may be neglected. Most audio
transformers fall in this class. Similarly, con-
sidering the secondary side of the transformer,
if the reflected generator resistance, or the
load resistance, is less than 20,000 ohms, the
secondary capacitance, Ca, may be neglected.
FIG. 8. Equivalent Network at Middle Fre- Though this is usually true of output trans-
quencies formers, it is seldom true of input or interstage
transformers.
The core-loss resistance, rc, has little effect at high frequencies beyond reducing the
secondary voltage by a few per cent. The per cent voltage drop caused by core loss, using
the symbols of Fig. 8, is
Core loss drop
100
rc/ra
per cent
(10)
This usually amounts to 2 or 3 per cent. As far as the shape of the response curve, or
the amount of phase shift, is concerned,
core loss may be neglected. rp rv 2(l-fc)L1 r2'
Neglecting primary inductance, pri- ^^r^AA/V — A/W^ — \J&SLQSL> — MAA/-
mary capacitance, and core loss, the
equivalent circuit, at high frequencies,
becomes as shown in Fig. 9. The term
2(1 — K)Lit is called the leakage induct-
ance referred to the primary and is usu-
ally designated by Le. FIG. 9. Equivalent Network at High Frequencies
OUTPUT TRANSFORMERS
6-17
9. OUTPUT TRANSFORMERS
The function of the output transformer is to transfer power from the plate, or plates,
of vacuum tubes to a load, such as a loudspeaker, an indicating meter, or a line. It provides
the necessary impedance transformation, and it isolates the load from the d-c potential
and current of the plate circuit. Efficiency is usually important, and the transformer
must meet a prescribed frequency-response characteristic.
TURNS RATIO is determined by the plate load recommended for the tube, or tubes,
by the tube manufacturer, rj/, and the actual load resistance, r&.
(11)
FREQUENCY RESPONSE is controlled by the amount of primary inductance, at low
frequencies, and by the amount of leakage inductance, at high frequencies. The allowable
drop at low frequencies fixes a rninimuin value of primary inductance. See Fig. 7 and
eqs. (6) and (7).
The equivalent network of the output transformer at high frequencies is given by Fig.
10, which is the same as Fig. 9 except that all capacitances have been omitted. The
i — vjQJL<t» — i ' — r™
T < >/
r R^**^ f2
FIG. 10. Output Transformer at High Frequencies
FIG. 11. Circuit Equivalent to Fig. 10
capacitance of an ordinary audio transformer winding will be about 100 ju^i/, more or less,
depending upon the coil construction. At 10,000 cycles, this is 160,000 ohms of capacitive
reactance. The load on an output transformer is seldom over a few thousand ohms and
may be as low as 3 or 4 ohms. The shunting effect of the secondary capacitance is there-
fore negligible, even at the highest audio frequencies. The reflected load, looking into
the primary, is seldom greater than 20,000 ohms, e.g., pushpull 6F6 tubes require 10,000
ohms. Again, primary capacitance is negligible.
The circuit of Fig. 11 is the exact equivalent of that of Fig. 10, as far as voltage output
and phase shift are concerned. The voltage output and the phase shift of all output
1 0
o
^.
p— -^_
n
— -^^^
"^-^
10
8
1 —
""\
^
"^
x
20 g1
3
j_ 7
\_
"\
X
s
i
) 6
4-
x
\
40 *?
3
a
o 5-
s
s
X. ^^
50 ^
>
) 4
CQ _
^>o^
.
V)
ts
60 f
3 3
in-
%\
^^
<n
70 g
12-
14
^
^^
80 Q
16-
^.
•~-«.
•^x
— «
1 — ,
•*+»
90
Q
100
1
^
ti
V
.«
.1
3
1
i :
•>
i
\
f.
I
J
1
0
Ratio Leakage Reactance /Resistance — ^fLe/Rf or Frequency Ratio=//f2
FIG. 12. Response and Phase Shift. Output Transformers at High Frequencies
transformers at high frequencies are given by this simple circuit, provided that the load
is resistive and the load and reflected load are less than 20,000 ohms. Figure 12 shows
those characteristics as a function of 2irfLe/R.
6-18 PASSIVE CIRCUIT ELEMENTS
At some frequency, 27rfLe — R, so that 2TrfLe/R = 1. Call this particular frequency /2.
This is the high frequency at which the response has dropped 3 db from its value in the
middle-frequency range. At twice this frequency 2irfLe/R = 2. At three times this
frequency, 2irfLe/R = 3, etc. At any frequency, /, 27rfLe/R — f/h. The curves given
in Fig. 12, as a function of 2x/Le/Jf2, are at the same time frequency characteristics, the
frequency being expressed in terms of the reference frequency, /2.
To determine the allowable amount of leakage inductance, it is necessary to know what
drop in secondary voltage is permissible, at some specified high frequency, as compared
with the voltage in the middle-frequency range. From Fig. 12, the ratio of 2irfLe/R
which gives this drop is found.
R = rp + n 4- JM' + rL'
Then
2irfLe R
^--B XW (12)
See F. E. Terman, Radio Engineering, 2nd Ed., pp. 293-299; L. A. Kelley, Transformer
Design, Rad. Engrg. (December 1934, February 1935) ; F. E. Terman and R. E. Ingebret-
sen, Output Transformer Response, Electronics, January 1936; and Magnetic Circuits and
Transformers, staff of M.I.T., pp. 472-486.
EFFICIENCY of output transformers is usually between 80 and 90 per cent, though it
may be as low as 60 per cent for cheap or poorly designed transformers. Maximum
efficiency is obtained, for a given physical size and core material, when copper loss = core
loss, and when primary copper loss = secondary copper loss. Such a balance of losses is
not always possible, however. If the secondary resistance, r%, is made 5 per cent of the
load resistance, rj,; if the primary resistance, n, is made 5 per cent of the reflected load
resistance, rif; and if the core-loss resistance, rc, is made 10 times the reflected load, ri/,
the losses will be very nearly balanced, and the efficiency will be 82 per cent. See eq. (9) .
LOUDSPEAKER LOAD. The analysis of output transformers given above has
assumed a constant, resistive load. If the load impedance is not constant throughout the
frequency range, the frequency-response characteristic will not be flat but will rise and
fall where the load impedance rises and falls. This effect is not very pronounced with
Class A triode amplifiers. However, with pentode or with Class B triode amplifiers, the
output voltage is approximately proportional to the load impedance. When such tubes
are used to drive the conventional moving-coil loudspeaker, a flat frequency-response
characteristic is no longer obtained.
The impedance-frequency characteristic of a moving-coil loudspeaker is characterized
by a low-frequency resonance peak and by a rise in impedance with frequency at the
higher audio frequencies. In the neighborhood of 400 cycles, the loudspeaker impedance
is the minimum and is resistive. This minimum, resistive impedance should be used as
the basis of calculating the turns ratio and the efficiency of the transformer.
Flattening of the frequency-response curve by mismatching, that is, by using a value
for rz, perhaps twice the value of the actual minimum, resistive impedance, in order to
favor the low and high frequencies at the expense of the middle frequencies, is somewhat
effective when used with Class A triode amplifiers. It does not level the voltage char-
acteristic but does tend to level the power output over a wider frequency range. Mis-
matching is futile, however, when used with pentode or Class B amplifiers.
The rise in impedance at the high frequencies may be offset by connecting a capacitor,
or a resistor and capacitor in, series, across the primary of the output transformer. The
low-frequency peak is best controlled by acoustical damping of the loudspeaker itself.
PTTSHPULL OUTPUT TRANSFORMER, CLASS A. No special problems are intro-
duced by pushpull operation of the output transformer if the amplifier is Class A. (See
Section 7, Amplifiers.) The generator resistance, rp, is twice the plate resistance of one
tube. The reflected load, rift is the recommended tube load, plate-to-plate. In fact, the
design of the transformer is simpler, for pushpull operation, because the d-c plate currents
of the two tubes flow in opposite directions in the transformer windings, so that d-c
magnetization of the core is canceled out. This results in higher primary inductance and
a better low-frequency response.
Data are furnished by the tube manufacturers on optimum plate-to-plate load. The
method of arriving at this optimum load is discussed by B. J. Thompson, Graphical Deter-
mination of Performance of Pushpull Audio Amplifiers, Proc. I.R.E., April 1933.
PUSHPULL OUTPUT TRANSFORMER, CLASS B. Class B operation imposes
special requirements on the output transformer, because one half of the primary works
during one half-cycle, and the other during the other half-cycle. It is important that the
two halves of the primary be closely coupled, so that the cross-over from one to the other
may be accomplished smoothly and without introducing transients. It is also important
that each half of the primary be coupled equally to the secondary. Otherwise the high-
INPUT AND INTERSTAGE TRANSFORMERS
6-19
FIG. 13. Arrangement of Windings, Clas
B Output Transformer
frequency response of the transformer will not be the same for both half-cycles, which
will produce even harmonics in the output wave. In general, leakage inductance should
be kept to the minimum between the windings of
a Class B output transformer, even beyond the re-
quirements of frequency response.
These requirements of low leakage and equal coup-
ling are met by using the coil construction illustrated
in Fig. 13.
THE MODULATION TRANSFORMER is an
output transformer, which has as its load the
plate of a Class C radio-frequency amplifier. This
load is resistive and is usually of the order of a few
thousand ohms. (See Section 7, Modulators.) The
audio-frequency generator is usually a Class B am-
plifier, so that the discussion of Class B output transformers given above applies to mod-
ulation transformers.
The secondary often is required to carry the d-e current of the Class C amplifier. This
produces a d-c magnetization of the core, which must be considered when designing the
transformer, because of its effect upon inductance and low-frequency response as well as
upon heating. Core saturation, due to d-c and a-c magnetization, is usually an important
factor in modulation transformers. It is most serious at the lowest frequency of the fre-
quency range, since there the a-c flux density is greatest. The effects of d-c magnetization
of the core upon inductance and upon saturation are discussed in Section 3, Ferrous-cored
Inductors.
Modulation transformers often work at high power levels, of the order of hundreds or
thousands of watts. Heating is an important consideration, as with power transformers.
Usually, too, high voltages are applied to the modulation transformer. The primary
center tap and one end of the secondary winding are connected to the d-c plate supply
and must be insulated to withstand its voltage. The ends of the primary and the other
end of the secondary, all of which are connected to plates, must withstand twice the d-c
plate supply voltage, since they have audio-frequency voltage, additional to the d-c
voltage, and of a peak value approximately equal to the d-c voltage.
Since the primary center tap and one end of the secondary are often connected to a
common point, the B supply, and since the load resistance of the Class C amplifier is of
the same order of magnitude as the reflected load on one tube of the Class B amplifier, there
is a strong temptation to make the modulation transformer an auto transformer, having
one half of the primary common with the secondary. The saving in size, cost, and insula-
tion by such construction is very great. Invariably, however, such construction leads to
trouble due to the unequal coupling between the two halves of the primary and the sec-
ondary. (See above, Pushpull, Class B.)
For a practical analysis of Class B modulation, and driver, transformers, see J. Kunz,
Transformers for Class B Modulators, Radio Engrg., July 1934.
THE LINE TRANSFORMER is not an output transformer, as it does not work out of
the plate of a vacuum tube. However, the analysis presented above for the output trans-
former applies equally well to the line transformer.
Turns ratio is determined in the same manner. Fre-
quency response and phase shift are governed by the
same factors, viz., primary and leakage inductances.
Line transformers usually operate at low power lev-
els, of the order of 6 milliwatts, or less, so that shield-
ing from stray magnetic fields may be necessary.
Often, too, it is necessary to balance the line to
ground. This means that the capacitance from one
FIG. 14. Balanced Coil Construction end of the primary to ground shall equal that from the
other, and the capacitance from one end of the second-
ary to ground shall equal that from the other. A symmetrical coil construction, as shown
in Fig. 14, accomplishes this purpose.
10. INPUT AND INTERSTAGE TRANSFORMERS
The function of the input transformer is to couple an audio-frequency voltage source,
such as a microphone, phonograph pick-up, or telephone line, to the grid of a vacuum tube.
That of the interstage transformer is to couple the plate of one tube to the grid of another.
Either type must conform to a predetermined frequency-response characteristic and must
furnish the greatest possible voltage amplification consistent therewith.
6-20 PASSIVE CIRCUIT ELEMENTS
With either type of transformer, the load consists of the grid circuit of a vacuum tube
(or tubes), and its impedance is very high, frequently of the order of megohms. It is
often no more than the input capacitance of the tube, although sometimes a resistor of
100,000 to 500,000 ohms is placed across the secondary, also. With such a high-impedance
load, the secondary winding capacitance is not negligible. The secondary winding capaci-
tance and the load capacitance, together, largely control the high-frequency response and
the turns ratio of the transformer.
FREQUENCY CHARACTERISTICS, LOW AND MIDDLE FREQUENCIES. The
same analysis applies to input and interstage transformers, at these frequencies, as applies
to other audio transformers. See above, Simplified Network at Low Frequencies and
Middle Frequencies. If there is no resistance load on the secondary, that is, if rif = oo ,
the equations given become simpler. Thus, eq. (8), for the secondary voltage, becomes
and eq. (9) , for efficiency, becomes
Efficiency = 0 (14)
FREQUENCY CHARACTERISTIC, HIGH FREQUENCIES. Figure 9 shows the
equivalent network at high frequencies. Considering first the case when there is no
secondary resistance load, the equivalent circuit becomes that shown in Fig. 15. This is
a simple series resonant circuit. It is convenient to express the performance of this circuit
by means of a family of curves, plotting voltage ratio vs. frequency, as shown by Fig. 16.
It is seen that the shape of the desired frequency-response characteristic determines the
value of a constant, N, while the position of the
rp r U, rr desired characteristic on the frequency band
2 determines the value of the resonant frequency,
/o. Then
£j = N(rp + n + raO (15)
FIG. 15. Input or Interstage Transformer at _ , . ,,-,,,
High Frequencies From these equations, the value of the leakage
inductance, Le, and of the reflected secondary
capacitances, C', which will give the desired frequency response, can be calculated. If the
amplification at high frequencies is to be substantially constant, the value of the cpnstant
N must lie between 0.75 and 1.0. See F. E. Terman, Radio Engineering, 2nd Ed., pp.
188-202; Gen. Elec. Tech. Report 19366, Audio Transformer Design (July 1930); and
Magnetic Circuits and Transformers, staff of M.I.T., pp. 486-494.
Considering the case in which a resistance load is placed across the secondary, in addition
to the tube input and secondary winding capacitances, the equivalent network is that of
Fig. 9. The resistance load will reduce the leakage resonance peak, at the same time lower-
ing the voltage output in the middle-frequency range in accordance with eq. (8) . How-
ever, the effect is more pronounced in the region of leakage resonance, so that an overall
flattening of the response characteristic results. See Terman, p. 199.
No single family of curves can be drawn which will show the performance of this circuit.
However, two methods of attacking the problem have been described. One method uses a
master chart showing the response at the leakage-resonance frequency. This chart
enables a designer to pick out a value of secondary loading resistance that will give the
desired response at resonance. He then computes the response at a few other points,
sufficient for plotting the frequency-response characteristic. See P. W. Klipsch, A.F.
Amplifier Circuits Using Transformers, Proc. I.R.E., February 1936.
Another method of solving the circuit of Fig. 9 is to draw several families of curves,
each family representing some fixed relationship between the various constants. This
method, with six such families of curves, is described by J. G. Story, Design of A.F. Input
and Interval ve Transformers, Wireless Engr., February 1938.
THE TURNS RATIO, of an input or interstage transformer is determined by the
secondary capacitance, that is, by the sum of the secondary winding capacitance, (?2, and
the input capacitance of the tube, CL- Call this total capacitance C, and let its value
reflected to the primary be C'. The correct value of Q' is found from the frequency-
response requirements, as described above. Then
INPUT AND INTERSTAGE TRANSFORMERS
6-21
The capacitance, distributed, and to ground, of the secondary winding cannot be
calculated accurately until the design of the transformer has been completed. As a first
approximation, for finding the turns ratio, a value of 50 MM/ may be used. The input
capacitance of the tube is given by the formula
CL « Cgf + Cfp(l 4- M)
where Cgf — static capacitance between grid and filament, Cgp — static capacitance be-
tween grid and plate, and M= effective amplification of tube.
.4 .5 .6 .8
Frequency
PIG. 16. Leakage Resonance
As an example of what can be expected in the way of turns ratio, assume that all sec-
ondary capacitances total 100 MMf and that the high-frequency response of the trans-
former is as given by N = 1 of Fig. 16, the resonance frequency being chosen as 10,000
cycles. The following step-up ratios are obtainable: with 10,000-ohm generator (triode),
1 to 4; with 500-ohm generator (line), 1 to 17.8; with 100-ohm generator (carbon mike),
1 to 40; with 0.2-ohm generator (ribbon mike), 1 to 890.
PICK-TIP AND SHIELDING. Input and interstage transformers often work at very-
low voltage levels. As a result, voltage induced in the windings by stray magnetic fields
may be as large as or larger than the signal voltage. These stray fields are produced by
nearby power transformers, rectifier filter reactors, open loops in wires carrying large
a-c currents, motor generators, etc. A hum of the frequency of the stray field is introduced
into the amplifier.
Correction of hum pick-up should begin at the source, if possible. Reduction of the
flux density in power transformers and reactors, by proper design, placing of air gaps of
reactors inside of the coils, use of shielding cans around power transformers and reactors,
and tight twisting of heavy-current wiring are all helpful.
Removal of the input, or interstage, transformer further from the source of disturbance,
and orienting it so that its coil will be at right angles with the coil of the disturbing trans-
former, are precautions that should be taken when laying out an amplifier.
6-22
PASSIVE CIRCUIT ELEMENTS
Input transformers are sometimes made with a two-legged core (see Section 3), half
of the primary and half of the secondary being placed on each leg. The two halves of
each winding are connected in series, being additive for flux within the core, but subtractive
for external fields. Such "hum-bucking" construction is very effective in reducing hum
pick-up, if the external field is uniform, so that it acts upon both parts of the transformer
equally. A reduction of 40 db in pick-up may be realized.
Shielding of the input, or interstage, transformer is also very effective in reducing pick-
up. A drawn nickel-alloy case with a tight-fitting lid will reduce pick-up about 30 db.
Two such nickel-alloy shields, one inside the other, separated by a similar copper shield,
will reduce pick-up by about 60 db. Three nickel-alloy and two copper shields will give
about 90-db reduction of pick-up. Such nested shields are available. See E. B. Harrison,
Notes on Transformer Design, Electronics, February 1944.
11. DRIVER TRANSFORMER
Function. The Class B operated output stage requires an auxiliary stage of audio
amplification called the "driver" stage. The driver transformer couples the plate of the
driver tube, usually a triode, to the grids of the Class B amplifier. The function of the
driver stage is to supply to the grid circuit of the output stage large positive voltage peaks,
which means that the driver stage is required to furnish power. In this respect the driver
transformer is similar to the output transformer, but it has additional requirements im-
posed upon it which make its design more exacting.
TURNS RATIO. The secondary load on a driver transformer varies over a wide
range during each half-cycle, from a very high resistance when both grids are negative to a
low resistance when either grid is positive. The turns ratio of the transformer must be
selected so that the change in load resistance has a negligible effect on driver tube distor-
tion, a condition which is satisfied by using a step-down ratio. The value of the turns
ratio is a compromise between distortion and driving power.
FREQUENCY RESPONSE is governed by the same factors as for the output trans-
former, viz., primary inductance at the low frequencies and leakage inductance at the
high frequencies. There is a difference, in that the load on the driver transformer is not a
constant resistance but varies during the cycle. Primary inductance should be high
enough to give the desired low-frequency response with n, = °o. Leakage inductance
should be low enough to give the desired response when TL = peak grid voltage swing/peak
grid current swing.
LEAKAGE AND DISTORTION. Leakage reactance in the driver transformer is a
reactance in series with the grids of the Class B stage. It causes distortion of the grid
voltage wave at the higher frequencies. The high-frequency range of a driver transformer
is limited by distortion rather than by a falling off of
the secondary voltage. Leakage between primary
and secondary must therefore be kept to the mini-
mum. It is also important that each half of the sec-
ondary be coupled equally to the primary; otherwise
the secondary voltage, at high frequencies, will not
be the same for both half-cycles, which will produce
even harmonics in the grid-voltage wave. The re-
quirements of low leakage and equal coupling are
met by using the coil arrangement shown in Fig 17.
See T. McLean, An Analysis of Distortion in Class
B Audio Amplifiers, Proc. I.R.E., March 1936.
Capacitances of the windings and input capacitance of the tubes have very little effect
upon frequency response or distortion. However, they may resonate with the leakage
reactance at some superaudible frequency to cause parasitic oscillations of the Class B
stage. Such oscillations cannot be suppressed by means of series grid resistors without
increasing distortion. It is desirable, therefore, to shunt a small capacitance from each
Class B grid to ground.
Fia. 17. Winding Arrangement, Class
B Driver Transformer
12. PHYSICAL DESIGN OF AUDIO TRANSFORMERS
Data Required. From the foregoing analyses of various kinds of audio transformers,
it is evident that the circuits which the transformer is coupling together must be clearly
and completely specified before a design of the transformer is attempted. The first step
in designing an audio transformer is to draw a diagram of the circuits, showing the values
PHYSICAL DESIGN OF AUDIO TRANSFORMERS
6-23
of generator and load impedance, direct current in any winding, and other pertinent data.
Next, the desired constants of the transformer, such as turn§ ratio, primary inductance,
leakage inductance, secondary capacitance, winding resistances, and core-loss resistance
are determined from the required performance of the transformer. Methods of finding
what constants in the transformer will give desired performance are described above.
DESIGN METHOD. There is no straightforward method of going at the physical
design of an audio transformer. The design is carried out by making several trials, each
one approaching closer to the desired constants. Procedure is as follows:
1. Assume a core size and a core material. As a starter, a core of El scrapless lamina-
tions (see Section 3, Ferrous-cored Inductors) , T/2 in. to 3/4 in. center leg, stack equal to
width of center leg, and silicon-steel material, might be chosen,
2. Calculate the number of primary turns that will give the desired value of primary
inductance (Ferrous-cored Inductors).
3. Multiply the number of primary turns by the turns ratio to give the number of
secondary turns.
4. Determine the primary and secondary wire sizes, using 500 circular mils per ampere
as a first trial, but not using wire smaller than No. 41 AWG. Extremely small and light
transformers may employ wire as small as No. 44, but these very small wire sizes should
be avoided, if possible, because of breakage when winding. If direct as well as alternating
current is present in a winding, the total current rms value will be
Itotal = Vide2 + /ac2
(18)
5. Lay out the windings. As a rule it is best to calculate the number of turns per layer
and the number of layers of each winding rather than to rely on some winding space
factor. The arrangement of windings may be fixed by some special requirements of the
transformer, as shown in Figs. 13, 14, and 17. Unless there is some reason for doing
otherwise, the primary is customarily wound first, with the secondary over It. (See
Inductors for details of construction.)
6. If the total calculated build of the coil, including spool, layer insulation, and wrapper,
exceeds 90 per cent of the window height, the core is too small, and steps 1, 2, 3, and 5
must be repeated, using either a larger core, a core with a larger window, such as the EE
scrapless style, or a core of better magnetic material. If the coil build is far below 90 per
cent of the window height, a smaller core should be tried.
7. After working out a core and coil that will fit and will have the desired primary
inductance and turns ratio, the other constants should be calculated from the design.
These include primary and secondary resistances, core-loss resistance, and leakage induct-
ance. In the case of input and interstage transformers, the distributed capacitance and
capacitance to ground of the secondary should also be calculated. In the case of high-
level output and modulation transformers, maximum flux density at the lowest frequency
(see Inductors), middle-range efficiency, and heating, should also be calculated.
8. Modify the design as required. An inspection of the first trial design will suggest the
changes needed. Leakage inductance and secondary capacitance can be varied consider-
ably by changing the arrangement and shape of the windings. Resistance of the windings
can be changed by using larger or smaller wire.
LEAKAGE INDUCTANCE depends upon coil geometry. For a two-winding trans-
former, as shown in Fig. 18, the leakage inductance, referred to the primary, is
Le
I
X 10~9 henry
(19)
in which c = length of a mean turn, a turn halfway between the innermost and outermost
layers; I = length of winding, or wire traverse; a = distance between windings, copper
to copper; di and dz are the build-ups
-I
of the two windings, all dimensions
being expressed in inches; and Np is
the number of turns of the primary
winding. The method of deriving this
formula is given by R. R. Lawrence,
Principles of A-C Machinery. Leakage
inductance, referred to the secondary,
is given by the same formula, except
that N/ is used in place of Np*, Ns be-
ing the number of turns of the second-
ary winding.
Core
Secondary Winding
Primary Winding
Margin
FIG. 18. Cross-section of Transformer Windings
6-24
PASSIVE CIRCUIT ELEMENTS
Leakage inductance can be reduced by dividing either the primary or the secondary
winding into two sections, placing the other winding between the two sections. One
arrangement is shown in Fig. 19a, in which the windings are concentrically wound. A
second arrangement is shown in Fig. 196, in which the windings are coaxially wound; this
construction is termed "pancake" winding. For the two cases:
ScNJ
heary
(20a)
(206)
(o)
FIG. 19. Interleaved Windings, (a) Concentrically Wound. (&) Coaxially Wound.
DISTRIBUTED CAPACITANCE of an audio-frequency transformer winding is made
up of the layer-to-layer capacitances. The turn-to-turn capacitances are negligible. The
equivalent capacitance across a winding is the resultant of the layer-to-layer capacitances,
in series. A winding of many layers, therefore, has less distributed capacitance than a
winding of few layers. The distributed capacitance, Cd, is
di*
micro-microfarads
(21)
in which c = mean length of turn of the winding; I — length of winding, or wire traverse;
d = distance between layers, copper to copper, all dimensions expressed in inches;
T = number of layers of wire in the winding; and k = average dielectric constant of layer
insulation, enamel, and impregnating compounds. For paper-insulated layers, k = 3,
approximately. See J. H. Morecroft, Principles of Radio Communication, 2nd Ed., pp.
233-235.
CAPACITANCE TO GROUND or between windings consists of the capacitances of the
inner layer and of the outer layer of a winding to surfaces which are adjacent to them.
The capacitances at the ends of a winding are usually negligible. Usually, one winding
is wound over another, concentrically, with 10 to 40 mils of insulation between them. Also,
the wire traverse is usually the same for both windings. The capacitance between the two
windings is the capacitance between two parallel surfaces, of the same area, having a very
small separation between them.
It is true that the a-c voltage between the two surfaces is not usually the same at all
points, because the a-c voltage across the outer layer of the one winding is usually not the
same as that across the inner layer of the other winding. Also, the capacitance calculated
between the outer layer of the one winding and the inner layer of the other is assumed to
be from the finish of the one winding to the start of the other. These are minor errors
if the number of layers on each winding is greater than 10.
If the mean circumference of the space between the two windings ~ c, length of
winding = Z, and separation of windings = d, all dimensions in inches, and k is the di-
electric constant of the insulation between them, the winding-to-winding capacitance,
Cwt is
a
. . . ,
micro-microfarads
,00.
(22)
The same formula may be used to compute other capacitances, such as that to core
to shield.
AUDIO TRANSFORMER MEASUREMENTS 6-25
13. AUDIO TRANSFORMER MEASUREMENTS
RESISTANCE. The d-c resistance is usually accurate enough at audio frequencies.
INDUCTANCE AND CAPACITANCE. Most iron-cored transformers for audio and
power frequencies resonate at some frequency in the neighborhood of 1000 cycles. This
is a parallel resonance of the mutual inductance and the winding capacitances. Measure-
ment of primary or secondary inductance or winding capacitance at 1000 cycles is meaning-
less. Primary or secondary inductance must be measured at some low frequency, 60
cycles being a convenient one, care being taken to apply an appropriate value of a-c
voltage and direct current. Bridges for inductance measurement are described in Sec-
tion 11.
Capacitance must be measured at some high frequency, such as 4000 cycles or above.
Any terminals which are normally at a-c ground potential should be grounded during such
measurements. A measurement of capacitance across any winding will include reflected
capacitances from other windings. If it is desired to measure the secondary capacitance
of an input or interstage transformer, this may be done indirectly by measuring the leakage
inductance and the leakage resonance frequency.
LEAKAGE INDUCTANCE is most conveniently measured on a 1000-cycle bridge,
short-circuiting one winding and measuring the inductance of the other. This frequency
is satisfactory since the mutual inductance and winding
capacitances are shorted out, leaving only the leakage in- I
ductance and winding resistances as factors in the measure-
ment. If the leakage inductance referred to the primary is 100(J
to be measured, the secondary is short-circuited and the in- oscillator*
ductance of the primary is measured. See Fig. 3, in which
Es would be short-circuited-
TURNS RATIO is most accurately and conveniently
measured with a bridge as illustrated in Fig. 20. Such a FIG. 20. Turns-ratio Bridge
bridge is as accurate as the resistance arms, except when
there is a large amount of leakage inductance in the transformer. Polarity is determined
at the same time as turns ratio. The windings must be additive in order to obtain a null.
CORE-LOSS RESISTANCE, in the middle-frequency range, referred to the primary,
is found by measuring the primary impedance, at the self-resonant frequency of the
transformer, with no load on the secondary. Figure 21 shows how this impedance may
be measured. This impedance is practically equal to
the core-loss resistance. Referring to Fig. 3, if £Li,
the primary inductance, is resonant with the total
capacitance Ci -}- CYj their combined impedance is
Osci la tor JU-r r- - ^e3[l|C — infinite, and they have no shunting effect on the cir-
I pjj I prj. oj |K Sec^ cuit. If rif and Cj/, the load resistance and capaci-
I L ylllC* _ tance, are removed from the transformer, the only
— I - >^ ' shunt left in the circuit is the core-loss resistance rc.
Vacuum-tube The series elements ri, the primary winding resistance,
Voltmeter _ Qf
FIG, 21, Measurement of Impedance ance, are usually very small as compared with re and
can be neglected.
FREQUENCY CHARACTERISTIC. An audio oscillator and a suitable voltmeter are
required. For measuring input or interstage transformers, the voltmeter must be of the
tube type, but for output transformers thermocouple or rectifier-type voltmeters may be
used. In any event, the voltmeter should not appreciably load the circuit being measured.
It is essential, when measuring frequency response or phase shift of an audio transformer,
that the circuits between which the transformer works, on the primary and secondary
sides, be either included in the measurement or that equivalent resistors, capacitors, etc.,
be used. A measurement of the transformer alone is meaningless. If the actual tube or
line on the primary side is not used, an equivalent resistor should be placed in series with
the primary winding.
Measurements should be made at an a-c voltage level corresponding to actual operating
conditions, and with direct current in the windings equal to any unbalanced direct current
under actual operating conditions.
6-26
PASSIVE CIRCUIT ELEMENTS
14. POWER TRANSFORMER
The function of the power transformer in radio and communication equipment is three-
fold: to insulate the equipment from the power line, to reduce the line voltage to the
voltages required by the tube heater circuits, and to step up the line voltage to energize
the anodes of the rectifier that supplies the d-c plate and bias voltages. The secondary
windings that supply voltage to heater circuits are usually called "filament" windings, and
the secondary winding that supplies voltage to rectifier anodes is termed the "plate"
winding, A typical power transformer might have a 115-volt 60-cycle primary, a 600- volt
center-tapped plate winding, a 5-volt 2-ampere filament winding for the rectifier heater,
and a 6.3-volt 3-ampere filament winding for the other heaters. Variations of this basic
pattern are, of course, very numerous, depending upon the voltages and currents needed.
Additional secondaries may be required to supply pilot lamps, relays, control motors, etc.
In transmitters, separate rectifiers may be used to supply plate and bias voltages, requiring
two plate windings. It may be desirable to turn on the heaters of large tubes for a warm-up
period before applying the plate voltage, which means that two separate power trans-
formers are required, one to supply the heaters, termed a filament transformer, and one
to supply the rectifier anodes, termed a plate transformer.
Power-line Frequency is 60 cycles per second throughout most of the United States.
In some parts of the United States and in many foreign countries 50 cycles is standard.
Most power transformers for radio equipment are designed for 50- and 60-cycle operation.
In aircraft, 400 or 800 cycles per second is often used.
VOLT-AMPERE RATING. The volt-ampere rating, of any secondary winding is the
product of the rms voltage, under load, by the rms current. The total volt-ampere rating
of all the secondaries is the sum of the volt-ampere ratings of the individual secondaries.
For a filament winding, the volt-ampere rating is simply a-c voltage times a-c current (in
amperes). Both voltage and current are of sinusoidal wave form, and the rms value of
each is the ordinary a-c effective value. For a plate winding, the rms voltage is the
ordinary a-c voltage, since the voltage wave is sinusoidal. However, the current in a plate
winding is not sinusoidal. Its rms value depends upon the amount of direct current
supplied by the rectifier, the kind of rectifier circuit used, and whether the first element
of the rectifier filter is an inductor (choke input) or a capacitor (condenser input). Table 1
gives the ratio of rms current, in the winding, to direct current, for various kinds of rec-
tifier. The factors given for capacitor input are round-number approximations, which
are accurate enough for most power-transformer designs. Actually these factors for
capacitor input vary widely, depending upon the resistance of the rectifier and the resist-
ance of the d-c load. For analysis of rectifiers see O. H. Schade, Analysis of Rectifier
Operation, Proc. I.R.E., July 1943; F. E. Terman, Radio Engineering, 2nd Ed., pp. 479-
500; R. W. Armstrong, Polyphase Rectification Special Connections, Proc, I.R.E., Jan-
uary 1931.
Table 1. Form Factors for Plate-winding Currents
Type of Rectifier
Heating Current
Volt-drop Current
Bridge, inductor input
Irms/Idc
1.0
n
1.0
Full- wave, pushpull, inductor input
Full- wave, pushpull, capacitor input. . . .
Bridge capacitor input
0.707
1.0
1.5
0.500
0.707
1 5
2.0
2 0
Voltage-doubler, capacitor input
3.0
3.0
SIZE OF POWER TRANSFORMERS is governed by heating rather than by efficiency
in most radio and communications work. Allowable heating limits the flux density in
the core and the current density in the windings. If the flux density is fixed, the core
cross-section is proportional to the volts per turn. See eq. (26), below. If the 'current
density is fixed, the core window area is proportional to the ampere-turns.
Core cross-section X window area is proportional to volts per turn X ampere-turns.
A X W - p ~ X
p(E X /)
(23)
wiiere A is the cross-section of the core, W is the area of the core window, p is a constant
of proportionality, N is the number of turns on the secondary of a transformer having but
one secondary, E and I are the rms voltage and current of this secondary, and E X / is
the volt-ampere rating of the transformer. When there are several secondaries, the same
POWER TRANSFORMERS
6-27
formula holds, but E X I is the sum of the volt-ampere ratings of all the secondaries.
Applying this formula to the common case of a 60-cycle power transformer, having 40
to 50 deg cent temperature rise, dimensions being in inches,
A X W = 0.024CE X I) approximately (24)
Power transformers often employ laminations of the El-scrapless shape (see Section 3r
Ferrous-cored Inductors). The core stack is often equal, or nearly so, to the width of
the center leg; that is, the center leg has a square cross-section. This core shape has a
0.1
30
40
60 70 80
Kilolines per Square Inch
FIG. 22. Core Loss. Silicon Steel at 60 Cycles
90
100
definite relationship between window area and core cross-section, W = 0.75A. Equa-
tion (24), for this case, can be simplified to
approximately
(25)
These formulas are fairly accurate for the average run of power transformers. However,
if operating voltages are high, or if the number of secondaries exceeds three, a larger
than usual part of the window is taken up by insulation, leaving less space for wire. To
allow for this, a somewhat larger core size should be chosen. Often, in such cases, a lami-
nation shape is desirable, having more window area than the El-scrapless lamination,
such as the EE-scrapless style.
CONSTRUCTION OF POWER TRANSFORMERS. Compactness is accomplished
by the use of a shell-type core, using laminations of the El-scrapless or EE-scrapless
shapes. Laminations are stacked alternately, or interleaved, one each way or two each
6-28 PASSIVE CIRCUIT ELEMENTS
way. Core material is almost always silicon steel having 2.5 per cent silicon content, or
higher. Lamination thickness may be 14-miI (U. S. gage No. 29), 19-mil (U. S. gage No.
26), or 25-mil (U. S. gage No. 24). The choice of silicon content and lamination thickness
is a compromise between cost and core loss, the lower silicon content and greater thickness
having the higher core loss. Core loss vs. flux density for several typical grades and thick-
ness of laminations are given in Fig. 22. See Ferrous-cored Inductors, for lamination
shapes, kinds of core material, and references.
Coil construction usually follows a conventional pattern, because a particular routine
of winding has been found to be most convenient. A single coil, which consists of the
various windings, is made, and is placed upon the center leg of the shell-type core. The
primary is wound first, over a formed spool of paper or fiber. The winding is layer wound,
with paper insulation between layers. Next, an electrostatic shield, consisting of one turn
of thin copper, the overlapping ends being insulated from each other, is placed over the
primary. The high-voltage or plate winding is wound on next. Up to this point, the
winding is done in multiple, ten or more coils being wound at a time. Generally, at this
point, the coils are sawed apart. The primary and plate windings ordinarily use wire of
sizes too small to be brought out of the windings as leads. So flexible, insulated leads
are anchored on top of the plate winding, the wire from the primary and plate windings
being brought around the ends of the windings and soldered to these leads. Then the
filament windings, which usually consist of a few turns of large wire, are wound on singly,
either one over the other or side by side, depending on the number of turns, wire size, and
wire traverse required. Generally the wires used for filament windings are sufficiently
large and rugged to be extended out of the windings as leads. See Ferrous-cored Inductors,
and also H. C. Roters, Electromagnetic Devices, Chapter VI.
The coil, or the core and coil together, are baked dry and impregnated with varnish,
wax, or asphaltic compound to exclude moisture, strengthen the coil mechanically, and
reduce lamination hum.
DESIGN PROCEDURE is relatively straightforward for power transformers, so that
design calculations are often made on a standard form sheet, or calculation sheet. Steps
are as follows:
1. Determine the rms voltages and currents of the secondary windings and the total
volt-ampere rating of all the secondaries.
2. Choose a core size which will satisfy eqs. (24) or (25).
3. Determine, approximately, the primary current. Assume 90 per cent efficiency and
90 per cent power factor as a first approximation. If the plate winding is not center-
tapped, the volt-ampere input to the primary will be
(Filament volt-amps + Plate volt-amps) -4- 0.81
If the plate winding is center-tapped, the volt-ampere input to the primary will be
(Filament volt-amps -f 0,707 Plate volt-amps) -r- 0.81
4. Calculate primary turns, Np.
(26)
in which EP — primary voltage, / = frequency, B = flux density in lines per square inch,
A — cross-sectional area of core in square inches, and k = stacking factor. Flux density
is usually around 70 kilolines per square inch, at the nominal primary voltage, for 60-cycle
designs.
5. Calculate secondary turns. Assuming a regulation of 10 per cent, as a first trial,
Ns = ^ X Np X 1.10 (27)
tip
If the number of turns on the low-voltage filament windings comes out fractional, the
turns on all windings should be increased or decreased sufficiently to give each low-voltage
winding a whole number of turns.
6. Determine wire sizes of all windings. The rule of 1000 circular mils per ampere is
very convenient to use as a first approximation and is usually not far from the correct
value arrived at in the final design.
7. Lay -out the windings. This is done by calculating the number of turns per layer,
the number of layers, and the build of each winding. See above, "Construction of Power
Transformers," and Ferrous-cored Inductors. Margins are usually 1/8 in. It is considered
good practice to use a double thickness of layer insulation between the two inside layers
and between the two outside layers of the high-voltage winding, to provide a factor of
safety against transients caused by line surges or switching. The total build of the coil,
POWER TRANSFORMERS 6-29
including spool, insulation, and outside wrapper, should not exceed 90 per cent of the win-
dow height.
Insulation between windings is determined by the operating voltage. The rule of twice
normal plus 1000 volts, for test voltage, is commonly used. Insulation must, of course,
be able to stand something more than the test voltage. The factor of safety allowed is
governed by cost and by the type of service which the radio or communications equipment
is required to give. For test voltages of 2500 rms or less, several thicknesses of Kraft
paper or two turns of varnished cambric are enough insulation between windings. Margins
of Vs in. are adequate for creepage. Above 2500 volts rms test, wider margins are neces-
sary as well as better insulation between windings. If, for example, the test voltage is
4000, and a two-to-one safety factor is allowed in the design, the margins must be wide
enough to withstand 8000 volts rms creepage. This requires about 7/i6-in. margins. A
point is reached where the margins required for creepage use up too much of the available
winding space. Such windings are insulated by wrapping them with half-lapped tape, of
varnished cambric, Fiberglas, or other insulating material. A narrow-windowed lamina-
tion or side-by-side sections of the winding are employed with very high voltage coils, of
1000 volts or higher, in order to keep the turns per layer and the voltage per layer low.
CALCULATION OF PERFORMANCE. The procedure outlined above will give a
design which is usually not very far from a satisfactory final design. It is necessary,
however, to calculate the output voltages of the secondaries, the heating, regulation, and
efficiency, and then to make minor adjustments in the design as required.
1. Resistance of each winding is calculated from the mean length of turn, in feet, the
number of turns, and the resistance of copper wire, of the particular size, in ohms per
1000 ft (see Section 2, for tables). The d-c resistance of the wire is used. An allowance
should be made for the fact that ordinary power transformer windings operate at tempera-
tures higher than 20 deg cent, usually in the neighborhood of SO deg cent. The resistance
of copper wire increases about 0.4 per cent per degree centigrade above 20 deg cent. The
mean length of turn, m, in feet, is given by
2(X + 7) - SR + 7r(2R + &)
(28)
in which X and T = inside dimensions of the winding, R = inside corner radius, and
6 — build of the winding, all dimensions being expressed in inches.
2. Copper loss of each winding is the rms current squared X resistance of that winding.
Total copper loss is the sum of the copper losses of the individual windings.
3. Core loss is the product of the watts per pound (Fig. 22) times the weight of the
core in pounds. Flux density, for determining watts per pound, is calculated from eq. (26) .
Actually, the flux density, under load, is somewhat less than given by this equation, owing
to voltage drop in the primary winding, but the error is very small. See Magnetic Circuits
and Transformers, Chapter V.
4. Heating may be calculated from the losses. There is no accurate formula for heating
of a power transformer in radio or communications equipment, because so many unpre-
dictable factors are involved. The proximity of other hot objects, such as rectifier tubes
or bleeder resistors, the amount of ventilation, the nature of the surfaces toward which
the transformer is radiating heat, whether dull or shiny, the kind of finish on the outside
of the transformer, and the characteristics of the potting compound, if the transformer is
potted, all influence the temperature rise of the transformer. However, a rough rule can
be worked out, based upon the Stefan-Boltzmann law for radiation from a black body,
which gives an approximate figure for temperature rise and is valuable as a basis for
comparing one transformer design against another. The radiation surface of a core and
coil is only slightly more than the total surface of the core, including window area. That
is, the coil surface adds very little to the radiation surface of the core and coil. E.g., if
the outer dimensions of a laminated core are 2 1/2 by 3 in. and the stack is 1 in., the total
core surface is 26 sq. in. This surface is very easy to compute from the core dimensions
and may be taken as the radiating surface of the core and coil. Calling this surface A,
in square inches, and the total watts loss W, the temperature rise in degrees centigrade,
AT, is roughly given by
(29)
See Magnetic Circuits and Transformers, Chapter VIII; Thermal Characteristics of Trans-
formers, V. M. Montsinger, Gen. Elec. Rev., April 1946; and R. Lee, Electronic Trans-
formers and Circuits, Wiley, pp. 37-44.
5. Output voltages of the secondaries under load, and the regulation of a transformer,
are calculated from tho resistances of the various windings. Voltage drop in a transformer,
6-30 PASSIVE CIRCUIT ELEMENTS
due to leakage reactance, is very small at 60 cycles and is usually not worth the trouble of
computing. An allowance of 1 per cent leakage-reactance drop is usually accurate enough.
The full-load voltage of the various secondary windings is obtained as follows :
A. Primary per cent IB, drop is
Pr, % = J,X*X100 (30)
&p
in which Ip = in-phase component of primary current = rms primary current -s- power
factor, ri — resistance of primary winding, Ep = impressed primary voltage.
B. No-load secondary voltages = impressed primary voltage X turns ratio, for the
various secondary windings.
C. High-voltage winding, full-load voltage is
X 0.99 (31)
in which EQ = no-load voltage of winding, lac = direct-current rectifier load, n = factor
depending on type of rectifier, and r% — resistance of high-voltage winding. The 0.99
multiplier is an allowance for leakage-reactance drop. Values of the n factor are given
in Table 1. To illustrate where the n factor comes from, consider a full-wave, inductor-
input rectifier with winding center-tapped. The direct current flows in one half of the
plate winding at a time, so the voltage drop in the plate winding is 0.5 X r% X /dc- The
value of n is 0.5.
D. Filament winding, full-load voltage is
X 0.99 (32)
in which EQ — no-load voltage of the filament winding, 1$ = rms load current, ra = resist-
ance of filament winding.
The regulation of each secondary winding, expressed in per cent, is
No-load volts — Full-load volts
TT 7i l 1 1 X -LUU
Full-load volts
Ordinarily, regulation is between 5 and 10 per cent.
6. Efficiency is the ratio, output watts -f- input watts. The output wattage of any
filament winding is simply the product of a-c voltage, under load, by a-c load current.
The output wattage of a plate winding is a complicated product of a sinusoidal voltage
and a non-sinusoidal current. As an approximation, multiply the rms voltage of the
total plate winding by the volt-drop current as given in Table 1. Then the output wattage
of the transformer is the sum of the wattages of the various secondaries.
Input wattage is computed by multiplying the no-load voltage of each secondary by its
rms load current if a filament winding, or by the volt-drop current if a plate winding, and
adding the core-loss watts. The efficiency of a typical power transformer is about 90
per cent.
16. VIBRATOR TRANSFORMER
Function. The vibrator transformer is used in radio and communications equipment
when the source of power is a battery instead of an a-c line. This occurs in mobile applica-
tions, such as automobile, aircraft, and railroad. The vibrator transformer takes the place
of the usual power transformer, supplying the proper voltages to rectifier anodes and to
heaters.
The center tap of the primary winding is connected permanently to one end of the
battery. The other end of the battery is connected alternately to one end or the other
of the primary winding by means of contacts on a vibrating reed. The frequency of the
reed is usually between 100 and 200 cycles per second, although frequencies as high as
400 cycles are used. This applies an alternating voltage, of square wave form, to the pri-
mary of the transformer. The frequency of this alternating voltage is, of course, the same
as the vibration frequency of the reed. The transformer is able to step this primary voltage
up or down, as required, in much the same manner as an ordinary a-c voltage.
An appreciable time is required for the reed to move from one side to the other, so that
the contacts are closed, one way or the other, only about 80 per cent of the time. The
transformer is connected across the battery only that percentage of the time. The portion
of the time that the vibrator contacts are closed is called the time efficiency of the vibrator.
VIBRATOR TRANSFORMER 6-31
A capacitor, called a "buffer" capacitor, must be connected across either the primary
or the secondary winding. Usually it is placed across the highest voltage winding because
a smaller value of capacitance will suffice there. The buffer capacitor is an essential part
of the transformer. When the correct value of buffer is used, it gives a smooth cross-over
^of the transformer voltage during the time interval when the vibrator contacts are open.
In so doing, it prevents sparking and high-frequency transients at the break and at the
make.
Often, heater circuits are connected directly to the battery, leaving only rectifier anode
voltage to be supplied by the vibrator transformer. The rectifier winding may be con-
nected to vacuum-tube rectifiers in the same
manner as the plate winding of an ordinary [ j ______ ^nfi J_Buffer Capacitor
power transformer. Or rectification may be
accomplished by using a second pair of con-
tacts on the vibrator which switch the load
back and forth across the secondary in syn-
chronism with the switching of the battery
across the primary. Figure 23 shows the
circuit of a synchronous vibrator trans- FIG. 23. Circuit of Synchronous Vibrator
former.
DESIGN. (Rectifier secondary only.) A. Core size is much larger than for an ordi-
nary power transformer of the same frequency and giving the same d-c voltage and
current. As battery voltage varies widely, flux density must be kept low. The primary
winding is almost twice as bulky as that of an ordinary transformer. The current is
flowing only part of the time, and so larger wire is required for the same average current.
On the other hand, if the frequency of the vibrator is much higher than 60 cycles, e.g.,
150 cycles, the higher frequency will reduce the size of the vibrator transformer. It will
still be somewhat larger than an equivalent 60-cycle power transformer.
B. Flux density and primary turns. The flux density in a vibrator-transformer core
is given by
S per s<3uare ^-^ (33)
in which EI = normal voltage of the battery, p — time efficiency, Np — total primary
turns, A — cross-section of core in square inches, k = stacking factor of core, and / = vi-
brator frequency. Flux density should be kept below 40,000 lines per square inch at
normal battery voltage. A still lower figure may be desirable at higher frequencies because
of core loss.
C. Secondary turns. As a first approximation, use
Ns = 1.33 X Np X ——d-c output v^0
p Battery volts
D. Current and wire size. The rms current in the secondary winding is
- (35a)
Vp
The rms current in the primary winding is
r 0.707 X /dc ^ N% /0,,,
J- p — 7^= X ~TT~ U>OO)
VP NP
in which JdC — d-c load current of the secondary. Wire sizes should be chosen to have
about 800 circular mils per ampere. Usually the primary has relatively few turns because
the battery voltage is a low voltage. The primary wire size should be chosen so as to give
2, 4, 6, or 8 even layers. This will place the center tap at the end of a layer, which is con-
venient for multiple winding.
E. Output voltage. The total resistance of the transformer and associated circuits,
referred to the working half of the secondary, is
TT~ \2 + r**TL) \N~P) +2 +Ts 0hmS (*36)
in which the r symbols indicate resistances, as follows: n - total primary, rv — vibrator
contact, TL = battery leads, rz = total secondary, and rg = rectifier tube, if any.
During the time that the vibrator contacts are closed, the secondary current
Then, the IR drop expressed in volts on the secondary is TT X
6-32 PASSIVE CIRCUIT ELEMENTS
The no-load d-c voltage across the first filter capacitor is
Eo = aE1 jjf (37)
jyp
a being a constant which takes care of imperfect contacts, primary and secondary contacts
not exactly synchronized, etc., = 0.94 for synchronous rectifier, 0.98 for tube rectifier.
Then the full-load d-c voltage across the first filter capacitor is
(38)
See T. T. Short and J. P. Coughlin, Try the Inverter Transformer, Mec. Mfg., June 1946;
F. E. Terman, Radio Engineering, pp. 500-501; Mallory Vibrator Data Book.
16. PULSE TRANSFORMER
In radar work, iron-cored transformers are used, which have voltage impressed upon
them for very short periods. These pulses are repeated at regular intervals, the time
interval between pulses being perhaps 1000 times the pulse duration. Analysis of such
pulse transformers cannot be made on a basis of Fourier analysis of the wave form because
of the relatively great time interval between pulses. Each pulse is a separate transient,
the effect of which dies out before the next pulse, except for core magnetization.
If a voltage is applied suddenly to the primary, through a generator resistance such as
the plate resistance of a modulator tube, then is held constant for a short time interval,
and then is suddenly removed, the input voltage will be of square pulse shape. The trans-
former will step up, or step down, this voltage, in accordance with its turns ratio, but the
output voltage will not faithfully follow the square pulse shape. An appreciable time is
required for the secondary voltage to build up from zero to its maximum value. This
"rise time" is caused by the leakage inductance and capacitance of the transformer. Dur-
ing the time that the input voltage is being held constant, the output voltage will be
falling off, the amount of drop from a constant voltage value being inversely proportional
to the primary inductance. When the input voltage is removed, the secondary voltage
does not drop instantly to zero but drags out
-Input Pulse through several damped oscillations caused
by the discharge of magnetic energy stored
in the core through the winding capacitances
and load resistance. Figure 24 illustrates
the kind of deformation of a pulse that oc-
curs when it is passed through a transformer.
See R. Lee, Iron-core Components in Pulse
FIG. 24. Deforming of Pulse Shape by Trans- Amplifiers Dromes, August 1943 and
former R- Lee, Electronic Transformers and Cir-
cuits, Wiley, Chapter IX.
The pulse transformer has a number of unique features. Because of the very low-duty
cycle, tremendous pulse power can be handled by a very small transformer. The require-
ment of low leakage inductance is met by close spacing between the primary and secondary
windings and by making the primary layer or layers exactly the same length as those of
the secondary, even to the extent of winding several wires in parallel on the low-voltage
winding. If a winding requires more than one layer, the conventional forward-and-back
method of winding is not used; layers are all started from the same end to minimize
capacitance between layers.
The small physical size and the relatively few turns which are essential to obtain low
leakage inductance together with very high pulse voltages make voltage gradients neces-
sary that are unheard of in ordinary transformer design. For example, 200 or more volts
per turn is not uncommon. This is accomplished by using Formvar-coated wire and im-
pregnating the transformer with transformer oil under a very high vacuum to remove
every trace of air.
High primary inductance is required, to keep the drop of voltage during the pulse to
the minimum. A new conception of incremental permeability is necessary in calculating
the inductance. All the pulses are of the same polarity; consequently the core is left in a
partially magnetized condition, owing to remanence. The hysteresis loop described by
the core has this remanent point as one of its ends. The shape of the loop is largely con-
trolled by eddy-current loss when the pulses are very short, such as of 1 microsecond
duration. Under these conditions incremental permeability is much lower than when a
INTRODUCTION 6-33*
core is operated with alternating current, and core material having low eddy-current loss
is desirable. Ribbon cores of very thin silicon-steel ribbon, 1 to 3 mils thick, are very
satisfactory for pulse transformer cores. Their incremental permeability under micro-
second pulse conditions is about 300.
ELECTRIC WAVE FILTERS
By A. J. Grossman
A wave filter is a device for separating waves characterized by a difference in frequency.
The general purpose of an electric wave filter is to separate sinusoidal electrical currents
of different frequencies. Ideally, a filter transmits freely the currents of all frequencies
lying within a specified range and excludes currents of all other frequencies. It may be
used to transmit the intelligence contained in a certain band and exclude adjacent steady-
state interference; combinations of filters may divide a wide frequency band into a number
of relatively narrow channels or may direct selected bands from one transmission path
into two or more different paths. Except in the simplest forms, a filter is a composite
network made up of several sections connected in tandem. Each section consists of
simple arrangements of two-terminal reactance networks. These reactances are provided
by combinations of ordinary coils and condensers, crystals, coaxial lines, and/or wave
guides.
The point of view developed by Bode, Campbell, Cauer, Foster, and others for the
analysis of a network is to regard the combination of inductances and capacitances as a
system excited by a vibratory disturbance to which the methods of particle dynamics can
be applied. It is convenient to express the analysis in terms derived from the classical
theory of wave propagation in continuous media. These terms are the image impedance
and the image transfer constant. In this terminology a filter is described as a system
having the following idealized properties. Signals lying within a preassigned frequency
band are transmitted without reduction in amplitude. This band is bounded by cutoff
frequencies at which there is an abrupt transition from free transmission to attenuation.
The attenuation increases more or less rapidly with frequency as the departure from a
cutoff increases. Concomitantly, the impedance is a pure resistance in the pass band and
changes abruptly at a cutoff to a pure reactance.
These idealized characteristics are approached in an actual filter inserted between
resistance terminations. The insertion loss for frequencies in the pass band remote from
the cutoff is essentially nil (apart from the effect due to dissipation in the components).
As the cutoff is approached the loss increases. The transition from the theoretical pass
band to the attenuating band is smooth. This transition interval can be made extremely
narrow in an elaborate design. The cutoff is not a frequency at which there is an abrupt
change from zero attenuation to a large value; it may mark the point at which there is a
rapid change from a small to a large value of attenuation, but at a finite rate. This de-
parture from the idealized characteristics arises from the fact that the filter is not termi-
nated in its image impedances. In simple cases, the image impedance varies considerably
with frequency, and, consequently, the input impedance of the filter has a non-constant
resistance component and an associated reactance component. By careful design the
image impedance may be maintained nearly constant over almost all of the pass band.
Nevertheless, there is still the smooth, but rapid, transition of the input impedance from a
predominantly resistive characteristic in the pass band to a predominantly reactive char-
acteristic in the attenuating band. The usual types of filters are low-pass, high-pass, and
band-pass.
17. INTRODTJCTION
A general filter network may be represented by a box, as in Fig. 1, having two pairs of
accessible terminals. The performance of this network is described in terms of its image
impedances and image transfer constant. The image imped-
ances are defined as those impedances with which the network 1 o-
must be terminated so that there will not be reflections at the 2 j x-
junctions 1—1' and 2-2'. That is, when the terminating im- lro
pedance £7 -is connected across 1-1', then the impedance FIG_ L A General p^ Net_
measured at the 2-2' terminals is Zj • and, similarly, when work
Zi^ is connected across 2-2', the impedance measured at 1-1'
is Zir The image transfer constant, 0, is defined to be equal to one-half the natural loga-
rithm of the ratio of the volt-amperes flowing into the network to the volt-amperes flowing
6-34
PASSIVE CIRCUIT ELEMENTS
ntege:
r~bO(
HH
HH
C
'2
-[(
Lzk+l '•
Ol = 1 . [•***••• -~.-['
ti Lcoicos • • • O)n_i-J
z =
Jco(w22 — co2) (co42 — w2) • • • (con-1 ~ w )
4-P) I
=cx =3
•"[(•^-^zlw*"''2-'"'^
'-[(
-Z^2A+1 =
052034 •••ton_
3
FIG. 2. Design Information for
out of the network when the network is terminated in its image impedances. These quanti-
ties are an exact measure of the performance of the filter only if the actual terminations
are equal to the image impedances. In a practical design, account must be taken of reflec-
tion and interaction effects arising from the mismatch between the terminating impedances
of the filter and its image impedances. These effects may be evaluated by the method
described in Section 5. They will not be considered in detail here. It will be assumed
that the performance of the filter is described by its image transfer constant.
By writing the mesh or nodal equations for the network, it may be shown that:
(1)
(2)
(3)
where ZA is the impedance measured at the 1-1' terminals when a short circuit is placed
across the 2-2' terminals, and ZQI is the impedance measured at the 1-1' terminals when
the 2-2' terminals are open. The short- and open-circuit impedances Z& and ZQ% at the
2-2' terminals are measured similarly.
INTRODUCTION
6-35
(3)
Z = 3-
; n = odd integer
HP
Ln-2
P^"1 Ln
pTRJtf> — o
LjlJ
C«.i
r ^ i ;
I— (o>2Jfc— 1 — Ur)Z J&>"<<>2jfc— 1
1,2, •- •
L! = B -
z-y-
n_22 - a:2) .
£2 £4
"
'2
Two-terminal Reactive Networks
The short- and open-circuit impedances are driving point impedances of a purely re-
active network. The requirements on such an impedance are (by Foster's theorem) :
It is an odd rational function of the frequency, OJ/STT, which is completely determined,
except for a constant factor, #, by assigning the resonant and antiresonant frequencies,
subject to the condition that they alternate and include both zero and infinity. Such an
impedance function may be physically realized by several canonical structures, among
them a combination of antiresonant circuits connected in series and a combination of
resonant circuits connected in parallel.
Figure 2 illustrates the four possible reactance functions which are distinguished by
their behavior at zero and innnite frequency. The series-type networks are specified in the
left-hand column, and the parallel type in the right-hand. The number of elements in each
configuration is the minimum, and equal to the number of critical frequencies plus 1.
The operations required to evaluate an expression such as
are to be performed in the following sequence: (1) multiply — by — •=
f ^ o)2jfc —
common factor (<w2Jb2 — co2) ; (3) replace co by cx^jt.
; (2) cancel the
6-36 PASSIVE CIRCUIT ELEMENTS
Illustration.
jw(o)22 — W2)(co42 — (02)
This is realizable with the second pair of networks. For the series type:
For the parallel type:
18. PROPERTIES OF THE IMAGE PARAMETERS
GENERAL CONDITIONS. In the pass band of a filter, the image impedances are
positive real quantities, or resistances; the image transfer constant is pure imaginary, which
signifies phase shift with zero attenuation. In the attenuating region, the image imped-
ances are pure imaginary, or reactances; the transfer constant has a positive real compo-
nent, which signifies attenuation.
COINCIDENCE CONDITIONS. According to eqs. (1) and (3), the image impedance
at one end of the network, and the transfer function, depend only on the short- and open-
circuit impedances measured at that end. Typical expressions for these impedances are:
H^aJ - co2) (q32 - co2) • • • (am* - co2)
41
where ai, as, 05, • • • are values of the angular frequency at which the short-circuited net-
work is resonant, and a2, a4, • • • are values of the angular frequency at which it is anti-
resonant. Similarly, the 6's with odd subscripts are the resonant, and the 6'a with even
subscripts the antiresonant, angular frequencies of the network when the far end is open-
circuited.
The expressions for the image impedance and transfer constant obtained with these
impedance functions are:
(ai2 - co2) • • • (am* - co2) (bi2 - co2) • • • (&fe2 - co2)
-co2 (a22 - co2) • • • (am_i2 - co2) (k2 - co2) - - - (bk^ - co2)
Ei (ai2 - co2) .-. (aTO2 - co2) (bg* - co2) • • » (bk^ - co2)
Ha ' (a22 - co2) ." (am-i2 - ^} ' (6x2 - co2) • - • (fefc2 - co2) U;
The statement of the general conditions on the image parameters indicates that the
network transmits freely when Zi* is positive and tanh2 0 is negative; it attenuates those
frequencies for which Zj* is negative and tanh2 0 is positive. In general, the expressions
(6) and (7) change sign as the frequency passes through each a and 6, and the network has
a multitude of pass and attenuating bands. In order that the network be a filter which
PROPERTIES OF THE IMAGE PARAMETERS
6-37
xx x 8
1
"3
i
oo 03*
1
^
eS^
1
^^
°3
* [E] {x] 3*
jT
1
I
^
3
"3
1
I
oxo 3*
1
Jj
I
^3
\
1
]
J
J
<T
(JiftA^ 1|
e§
X 0 X 3"
I
3
3
Nf
^
1
3
I
ft
1
f
*~s
3
*v
C4
T3
d
oxo 3"
°3
i<
*%.
^3
I
^
M«
3 1 1
3,
/J
«
x [x] [x| 3*
1
"3
°3
I
I
I
Is
•ft'
i
Hi
O O O 3
XX X 0
I
i
*v
•^
1 i-i
1
hn
.5S()r_i}_r"
* O j- •£"'
°"-<
**•*
J5
[5
>
NJ M c M
3
^
*
^ "
"*"'
t?
rsT
!
oxo 8
?
X o x 3*
(
^T
*c
^Mj
cT"
^5-
1
^T
I
3
_,_^
T3
OXO 3*
I
f
Jf
I
3
to
1
1
r
1=
i
x O x 3°
j;
M«
°3
%.
^
M-
\
e_
_r
&
^5-
1
•*~s
3
3
^~
-a
5
, . _ N
x [0] 0 3
i
1
1
\
1
t*
I
J
3
•>>
vOQ(L
£
00 03
j]
J
|
3*
a
J
XX X 0
£
•^
-$>
IS*
IB
>
^ o ^ H?
"1
^7^
— i_Qp_Qj 1|
M NJ c Nl
to
5SJ
N?
!
0 0
o o 08
J
10
eT*
3
§
xx X 3 ^
3
«^
?
"^3
1
cT*
^-s
«
1
o (o] [oj 3"
1
1
3
1
^3
"i
1
09
,3,
^3
1
11
1
X O X 3
3
°?
J
"t
*S
cT
"3
CN
^
a
1
K
1
oxo 3
1
**«
1
3
J
1
i
|
I
3*
„
'
x o x 3
3
^
^3
3
1 1
5"
"
-£
1
^
|
>
i- —
j —
oxo o
£j
*%
^
"*
[^j^
ij=
5 0 ^ >^
o
s
^^
NT
a
£
la
§|
^
O
"a
^
1 |
f_,
^5
^5
5
^5
O "^
.2
£ ft
P4 §
g
fci
6-38 PASSIVE CIRCUIT ELEMENTS
passes one continuous band of frequencies and attenuates all other bands, it is necessary
to place certain evident restrictions on the critical frequencies of its short- and open-circuit
impedances. If, for example, ai = 61 = coi, the factors («i2 — co2) and (&i2 — co2) cancel
each other in tanh2 6 but form the factor (coi2 — co2)2 in Zjf. In either event, as co passes
through the value coi the sign of the expression does not change. It follows that the
elements of the network must be so chosen that all the a's are equal to, or coincide with,
6's except possibly in two cases. These exceptional cases correspond to cutoff frequencies
at which the network changes from a condition of free transmission to attenuation, or vice
versa. These transition points may be two a's or two b's or one a and one 6.
For the typical short- and open-circuit impedances under consideration, it is seen from
(6) and (7) that Zi^ is negative and tanh2 B is positive at zero frequency. That is, the
filter attenuates zero frequency. This condition will continue over a frequency band pro-
vided that ai = 61, «2 — bz, or, in general, a3 = bj. The attenuation band is terminated
at a cutoff frequency by locating an a at that frequency without a corresponding 6, or
vice versa. In either case, if a continuous pass band is to extend beyond the cutoff, it is
necessary that the subsequent coincidences of critical frequencies be of a type specified
by the formula a, = 63±i, since the sequence either of a's or of b's has lost a step at the
cutoff. The pass band may continue to infinite frequency or it may be terminated at a
second cutoff. This cutoff may be specified by either an a or a b. Then the coincidences
in the attenuating band above this cutoff are given by the formula a? = bj or a/ = bj±z.
The first relation holds if one cutoff is an a and the other a &; the second, if both cutoffs
are a's or b's.
Inspection of eqs. (6) and (7) leads to the following conclusions: (a) coincidences of the
type a,- = bj and a, = bj±% produce double zeros or poles in Z/x2 but cancel out in tanh2 6;
(6) coincidences of the type a, = 63-±i produce double zeros or poles in tanh2 6 but cancel
out in Zi*\ (c) critical frequency coincidences of the first type produce image-impedance-
controlling factors; those of the second type produce transfer-constant-controlling factors.
SUMMARY OF PROPERTIES OF THE IMAGE PARAMETERS.
1. Tanh2 0 is the ratio of two impedance functions of a reactive network, and Z/2 is the
product of two such functions. Tanh2 B and Zp contain only double zeros and poles except
possibly for two zeros or poles, which are simple.
2. The simple zeros or poles represent cutoff frequencies and occur at positive values
of co2. They are the same for the two expressions except for the possibility that either or
both may be a zero in one expression and a pole in the other.
3. The zeros and poles of tanh2 B alternate with each other in each continuous pass
band; the zeros and poles of Zp alternate with each other in each continuous attenuating
band. The step between bands may interrupt the alternation since the cutoffs may both
be zeros or both poles.
Illustration. Examples of expressions for the short- and open-circuit impedances and the image
parameters are given in Fig. 3. The frequency pattern is a convenient schematic representation of
these functions. It is a plot of the location of the zeros and poles of a function in the frequency scale.
The conventions are: circles denote zeros of the function (or resonances of the impedance); crosses
denote poles of the function (or antiresonances of the impedance); squares represent cutoffs. These
diagrams serve to illustrate the properties of the image parameters summarized above. The network
configurations shown in the table are "possible" in the sense that they will be obtained for an appropriate
choice of the multipliers HI and Hz and the critical frequencies of the short- and open-circuit impedances.
19. OPEN-CIRCUIT TRANSFER IMPEDANCE
Two important filter theorems, due to H. W. Bode, can be derived from the properties
of the open-circuit transfer impedance. This impedance, designated #012, is the ratio of
the voltage appearing across the open output terminals of the network to the current fed
into the input terminals. For a purely reactive network, this impedance function has real
coefficients and is imaginary at real values of frequency. It is expressed in terms of the
short- and open-circuit impedances by:
By use of eqs. (l)-(3), this may be written:
/i \
(9)
Since #012 is imaginary along the real frequency axis, Zoi22 must be negative there. Conse-
quently, if ZiZi^ changes sign, then - — r-^- — 1 must change sign at the same time, and
tann \j
conversely.
IMAGE IMPEDANCE THEOREM 6-39
In the pass band, the image impedances are resistances, and the transfer constant is
imaginary, and so the requirement on Z0i22 is satisfied. In the attenuating band where
the image impedances are reactances, and tanh 6 is real, there are two possibilities:
(a) If the image impedances are reactances of the same sign, the product Zi1Zr2 is
negative. Therefore, tanh 6 must be equal to or less than unity. This interval will be
called a type I attenuating band and will be designated ABI.
(b) If the image impedances are reactances of opposite sign, Z^Zj* is positive. There-
fore, tanh 6 must be equal to or greater than unity. This interval will be called a type II
attenuating band and will be designated ABII.
20. TRANSFER CONSTANT THEOREM
The transfer constant of any physically realizable filter is uniquely determined by the cutoff
frequencies and by the frequencies of infinite attenuation.
The frequencies at which the attenuation is infinite are the roots of the equation
tanh 0—1. In practice, they are found by determining the roots of the equation
tanh2 0—1 = 0. The number of roots in terms of c^2 is equal to the number of pole-zero
intervals of tanh 6 in the pass band or, equivalently, the total phase shift in radians divided
by 7T/2. From a consideration of the properties of the open-circuit transfer impedance,
it is deduced that the admissible roots of a physically realizable filter are the following:
(a) roots of even multiplicity located at positive values of o^; (6) roots of even multiplicity
located at negative values of oj2; (c) roots of even multiplicity located at conjugate complex
values of co2; (d) roots of odd multiplicity located at positive values of co2. As the later
discussion shows, filter sections having roots of even multiplicity are the rule rather than
the exception. They are symmetrical sections, for which the restrictions on the image
impedance are the minimum. They are usually designed to have the simplest image
impedances.
There are two additional restrictions on the expression for tanh 6: (a) If zero or infinite
frequency lies in a pass band, tanh & must have a zero at this frequency; (6) if zero or
infinite frequency lies in an attenuating band, tanh 6 must be equal to or less than unity
at this frequency; in particular, tanh 9 — 1, if this frequency lies in an ABIT.
The significance of the above theorem is that if an expression for tanh 6 is found which
contains the chosen cutoff frequencies, and is equal to unity at the chosen (admissible)
frequencies of infinite attenuation, it is the only such expression that does exist, and it will
lead to a physically realizable filter. Such an expression can always be found.
Illustration, (a) Test the expression
tanh 6 •
for physical readability. The equation tanh 0—1 has two roots. By forming
tanh2 0 - 1 = , -1^» - 0
(1 — 6J2)2
both are found to be located at <w2 = «. Therefore, this expression has a physical representation,
(b) Test the expression
for physical readability. From
it is seen that there is a single root at to2 = — 1 and another at o>2 = «. Therefore, this expression
for the transfer constant is not realizable.
21. IMAGE IMPEDANCE THEOREM
The second image impedance of a fitter is uniquely determined at aU frequencies, except for
an arbitrary constant multiplier, by the transfer constant and the first image impedance.
This theorem may be demonstrated by an examination of the properties of the open-
circuit transfer impedance. The formation of the expression for the second image imped-
ance is accomplished by the application of the following rules:
(a) At the boundary of a pass band and ABI, the cutoff factor appears in the numerator
of tanh 6 and in the numerator or denominator of both Z;l and Zj^.
6-40
PASSIVE CIRCUIT ELEMENTS
(6) At the boundary of a pass band and ABII, the cutoff factor appears in the denom-
inator of tanh 6 and in the numerator of one image impedance and in the denominator of
the other image impedance.
(c) At the boundary, ABI/ABII, of the two types of attenuating bands, the equation
tanh2 0 = 1 has a root of odd multiplicity One image impedance must have a zero, or
pole, at this frequency which does not appear in the other image impedance.
(d) All other zeros and poles of one image impedance give rise to corresponding zeros
and poles (or poles and zeros) in the second image impedance. Attention must be given
to the requirement that the zeros and poles of each impedance alternate in an attenuation
band.
(e) Roots of even multiplicity can be introduced in (tanh2 0 — 1) without regard to the
image impedances.
Illustration. The expressions for the transfer constant and the image impedance at one end of a
band-pass filter are:
tanh Q •
h - ay*
where <ui is the lower cutoff, and &>2 the upper cutoff. The region from zero frequency to o>i is an .451,
and, by rule (a), the cutoff factor corresponding to «i appears in the denominator of Z/2. The region
from o>2 to infinity is an AJBII, and, by rule (6), the cutoff factor corresponding to W2 appears in the
denominator of Zj^. The expression:
has one root in w2, and that is at infinity. Thus, there are no other internal zeros or poles in Ziv
Finally, with the aid of rule (d),
»„-.
The elements of the filter may be found from the short- and open-circuit impedances:
H
1 o — IftRP-
Zai = Zil tanh 6 => Hju
I'O-
J. 1
-o2'
Kju
FIG. 4. Illustration for the Method of Obtain-
ing the Second Image Impedance from the
Transfer Function and the First Image Im-
pedance
tanh e
_, ,,,.-,, ^ . ^
Tbe network obtained by setting K =
shown in Fig. 4.
22. THE GENERAL COMPOSITE FILTER
As exemplified by the preceding illustration, a possible filter design method consists of
setting up physically realizable expressions for the desired transfer constant and image
impedance at one end of the filter. Then, the expression for the second image impedance
is found with the aid of the rules associated with the image impedance theorem. The
corresponding short- and open-circuit impedances are computed. From these, it is possible
to find the elements of the filter. In general, this may require some ingenuity.
The design method which is used most frequently is based on the fact that every filter
can be regarded as the
combination of certain ele- 1 °~
mentary sections. As —
shown in Fig. 5, the com-
posite filter is made up
of -TV elementary sections
connected in tandem. Sec-
tion A provides one or
lo-
N
-o2
FIG. 5. The General Composite Filter
more frequencies of infinite attenuation (in terms of to2) and has the image impedance Z^
specified for the input side of the filter. The secondimage im pedance Zia is deter-
mined by Zi1 and the roots of (tanh 6 = 1) provided by section A. Section B has
SYMMETRICAL SECTIONS
6-41
the image impedance Zja to match A and provides one or more of the remaining fre-
quencies of infinite attenuation. Its other image impedance is Ziy The last section has
the image impedance Z/2, consistent with the specification of Z^ and all the frequencies
of infinite attenuation, that is, all the roots of tanh 0=1.
The first step in the application of this design method is the selection of the terminating
sections to furnish the desired image impedance. They provide a simple image impedance
(i.e., one without impedance controlling factors) at their inner pairs of terminals. These
sections correspond to A and N in Fig. 5. The transfer constant contributed by these
sections is subtracted from the required overall transfer constant. The balance is supplied
by elementary sections of known transfer constant characteristics which have simple image
impedances. These are inserted between the terminating sections.
An alternative design procedure is applicable where it is convenient to establish a
physically realizable expression for the transfer function, tanh 6, which meets the require-
ments of the design objective. Such a case arises, for example, if the objective is to attain
linearity of phase over the pass band; another objective which can be handled in this way,
as will be described later in this article, is to provide a prescribed minimum of attenuation
over a specified interval of the attenuating band. The next step in the design is the
determination of the frequencies of infinite attenuation by solving the equation tanh 6 — 1.
Then these frequencies are assigned to the appropriate elementary sections, and the sections
are assembled to form a composite filter.
These design procedures are facilitated if there is available a list of the characteristics
and element values of the elementary sections and the terminating sections. Such a
tabulation should contain sections which provide double positive and negative roots in co2,
double pairs of conjugate complex roots, simple positive roots. In general, the double
roots correspond to the elementary symmetrical sections which form the main body of
.the filter, and the simple roots correspond to the unsymmetrical sections which are used
for terminations. The tabulations of these sections are discussed in the following two
paragraphs.
23. SYMMETRICAL SECTIONS
The problem associated with the design of symmetrical filters is much simpler than the
general design problem. The configuration which is convenient for analysis is the lattice,
shown in Fig. 6. From the fundamental eqs. (l)-(3)
for the image parameters, it may be shown that:
(11)
By identifying Zx with Zs\, and Z>y with ZQI, the anal-
ysis in terms of critical frequencies, given in article 18,
is directly applicable. The restrictions on Zi and tanh
0/2 are simply those summarized there for Zi and
tanh 0. The only distinction is that the resulting
transfer constant, 0, of the lattice is twice the value
0/2 appearing in eq. (11). The restrictions contained pia 6 The General Symmetrical
in the transfer constant and image impedance theo- Lattice Configuration
rems are satisfied since all the roots of (tanh 0=1)
are of even multiplicity. This means that the expressions for the transfer constant and
image impedance can be chosen independently except for the cutoff frequencies which are
the same in the two expressions. The branch impedances are:
Zx = Zi tanh -
2
tanh (0/2)
(12)
(13)
These impedances satisfy the requirements of Foster's theorem and may be developed into
the structures listed in Fig. 2.
It is evident that these branches will contain a large number of elements for all but the
simplest filters. Since attenuation is obtained by bridge balance, these elements must
be held to close limits if the required attenuation is great. Consequently, though the
lattice is much used in theoretical work, it is usually converted, when possible, to other
configurations. The first step in the conversion process is to apply the concept of the
6-42
PASSIVE CIRCUIT ELEMENTS
-ww-
is
2
< z
FIG. 7. Conversions of the Symmetrical Lattice
SYMMETRICAL SECTIONS
6-43
(1)
(2)
(3)
(4)
HH
=
c2
mR
mR
mR
mR
(1 - m2)
2mvfcR
Ci
< 1
V
-&
0 <m < oo
' /oo
0 <m < I
v
-
0 < m < oo
impedance
fc
Same as (1)
V/c2 -
Same as (3)
jmf
Same as (1;
Same as (1)
Same as (1)
Special case
m — I
/co- «>
1/2 = short circuit
L2
Ci = open circmt
= C2
FIG. 8. Design Information for Elementary Symmetrical Low-pass Filter Sections
(D
(2)
(3)
(4)
II— «
mR
Ci
Im-xfcR
.
/c2
0 < m < oo
/c2
< oo
Image
impedance
Zi
Same as (I)
Same as (3)
tanh-
w/c
Same as (I)
Same as (1)
Special case
m = \
= short circuit
Ci = C2
LI = open circuit
LI = L2
FIG. 9. Design Information for Elementary Symmetrical High-pass Filter Sections
6-44
PASSIVE CIRCUIT ELEMENTS
*•••* Q
<u ^
a v
^_^ o
^ v
LaaiJ
o
*s
•is
1
SYMMETRICAL SECTIONS
I !
s
£v
6-45
-fh
Hh
^000 .
f
S^
sv
4
i
lv
020
v
.§*?
•3 a a
5
g
2
£
6-46
PASSIVE CIRCUIT ELEMENTS
^s
€V
e:
CT=|= N g
^SWU 1|—
1 V
vi
-IS
as
SYMMETRICAL SECTIONS
6-47
I v
e> §
S V
!*
£ vi
S vi
6-48
PASSIVE CIRCUIT ELEMENTS
composite filter. Then, after the original lattice is separated into a combination of the
simplest lattices, these, in turn, are converted to other configurations. Some of the most
useful conversions, based on Bartlett's bisection theorem, are given in Fig. 7. (Broken
lines are used to simplify the drawings. It is understood that the lattice branches repre-
sented by these lines are duplicates of the corresponding ones shown explicitly.)
ELEMENTARY STRUCTURES. The elementary symmetrical sections which pro-
vide the double positive and negative roots required in forming a composite filter are
listed in Figs. 8, 9, 10. Since a double root of (tanh2 0—1) corresponds to a simple root
of ( tanh2 - — 1 J , it is possible to use the more convenient expression, tanh (0/2) , in
describing these sections. Each of the configurations provides one double peak of infinite
attenuation. The associated image impedances are the simplest possible. The transfer
constant, 0 — a. -f- y/3, where a is the attenuation constant in nepers, and /3 is the phase
constant in radians, is computed from the expression for tanh (0/2). If the arithmetical
value of this expression is denoted by Q, then, in the pass band:
(9
tanh - = jQ
In the attenuating band:
j3 = 2arctanQ; (—>
tanh- = £; (Q > 0)
There are two possibilities, depending on the value of Q relative to unity. Either:
a. = 2 arg tanh Q; (Q < 1)
B - 0
o: «s 2 arg tanh - ; (Q > 1)
|8 = ±7T
The element values specified in these tabulations, as well as all that follow, apply to the
filter sections as drawn. That is, each section is considered to be a building block in the
composite filter. For example, if two lad-
der-type mid-series terminated sections
having the same image impedance are
joined together, the intermediate series
impedance becomes equal to the sum of
the values given in the figures; similarly,
if two ladder-type mid-shunt terminated
sections are joined together, the inter-
mediate shunt admittance becomes equal
to the sum of the values given.
Figures 8 and 9 contain the design in-
formation for low-pass and high-pass sec-
tions, respectively. The cutoff frequency
is denoted by fe and the frequency of in-
finite attenuation by fw. The image im-
pedance is equal to R at zero frequency
for the low pass, and at infinite frequency
for the high pass. The sections numbered
(1) and (3) provide double peaks of atten-
uation at real frequencies. They are the
m-derived sections introduced by O. J.
Zobel. The special case for which m = 1
is the constant-jK" section. Sections (2)
and (4) provide double peaks at real fre-
quencies for values of the parameter m
lying in the range 0 < m < 1, and dou-
ble peaks at imaginary values of frequency
FIG. 11. Combination of Two Lattice Sections ^'e" negative values of co2) for values of
Which Have the Same Image Impedance m greater than unity.
SYMMETRICAL SECTIONS
6-49
The elementary band-pass sections are shown in Figs. IQa and b. The lower cutoff
frequency is denoted by /i, the upper cutoff by /2, and the peak of infinite attenuation
by /co- The image impedance is equal to R at the mid-band frequency, fm = Vf&. A
Type
Image Impedance
Configuration
Low-pass
Rfc
High-pass
jfR
- A)
jf(h-fi)R
Band-pass
FIG. 12. Elementary Constituents of the General Composite Filter Which Provide Attenuation Peaks
at Complex Values of Frequency
uniform definition for the parameter ra is used throughout, with the result that the range
of values is extended beyond the conventional zero to unity. The odd-numbered sections
in Fig. 10a correspond to the usual m-derived sections which have a peak of attenuation
below the lower cutoff. The special cases, for which m = 1, are the so-called three-
element type band-pass sections having a peak at zero frequency. The lattice sections
6-50 PASSIVE CIRCUIT ELEMENTS
provide a peak below the lower cutoff for 0 < m < 1, and a peak above the upper cutoff
for /2//i < m < oo . For the range 1 < m < /2//i, the peak is located at an imaginary
value of frequency. In all cases, the phase shift is ( — x) radians at f\ and zero at /2.
The odd-numbered sections in Fig. 106 correspond to the usual m-derived sections which
have a peak of attenuation above the upper cutoff. The three-element type sections having
a peak at infinite frequency are special cases, for which m — fz/fi. The lattice sections are
the same as those shown in Fig. 10a except that the branches are interchanged. In all
cases, the phase shift is zero at A, and (+w) radians at /2.
The elementary sections which provide the double pairs of conjugate complex roots
have a double peak of attenuation at the complex value of frequency, /„, and a double
peak at the conjugate value, /,». They can be derived by combining two lattice sections
of the type tabulated in Figs. 8—10. The method for combining two symmetrical lattice
sections which have the same image impedance is shown in Fig. 11. By using the defini-
tions for the parameter in given in the previous figures, a complex value, m = mi + jmz,
is obtained for the section which provides the peak at the complex value of frequency, /^j
the conjugate complex value, m = mi — jmz, is obtained for the section which provides
the peak at the conjugate complex value, 7^. (The real part, mi, must be positive.) The
elements of the individual lattice sections are proportional to m and m, and their recipro-
cals, and therefore are complex quantities. However, upon combining the two sections,
the resulting elements are ordinary coils and condensers. These sections are displayed
in Fig. 12.
24. UNSYMMETRICAL SECTIONS
The unsymmetrical sections provide the simple positive roots of (tanh2 0 — 1) in terms
of to2. Generally, they are viewed as the means for converting the simple image impedance
of the main part of the composite filter into an image impedance which approximates as
closely as required to a constant value, equal to the resistance in which the filter is termi-
nated. For low- and high-pass filters, the conversion is from a constant-,?? type "image
impedance to one having one or more impedance-controlling frequencies. For band-pass
filters, there is a greater variety of possibilities. However, as a practical matter, the
terminating sections are usually designed to convert a constant-.^ image impedance into
one having one or more pairs of impedance-controlling frequencies. The product of the
frequencies making up a pair is equal to the square of the mid-band frequency. For com-
pleteness, it is necessary to have available the simple sections which convert a three-
element type image impedance into the geometrically symmetrical constant-^C type.
The design information for the simple sections which are used to obtain either a mid-
series or mid-shunt constant-.^ image impedance is given in Fig. 13. They are all "half-
sections," and the element values apply to the sections as drawn. Comparison of the
formulas for the element values and image impedance of the three-element band-pass
sections with those given for the special cases in Figs. 10a-Z> shows that they differ by a
factor which is a function of the cutoff frequencies. This arises from the fact that the
symmetrical sections are designed to give an image impedance equal to R at the mid-band
frequency, while those in Fig. 13 satisfy this condition only at the constant-^ end of the
structure. Hence, the impedance level of one or the other must be changed by the factor
specified in the lower part of Fig. 13 before they can be joined without reflection. In
general, the level of the symmetrical sections is changed so that the constant-jfiT impedance
of the terminating section has a mid-band value equal to the termination. For example,
the inductances of sections 7 and 8 of Fig. 10a are multiplied by the factor C/2 + /i)//2,
and the capacitances divided by this factor, if the section is joined to the first band-pass
section of Fig. 13.
m-DERIVED SECTIONS. The design information for terminating sections which
present a constant-.^ image impedance at one end and an image impedance having one
controlling frequency (or one geometrically symmetrical pair) at the other end is given
in Fig. 14. It follows from the rules associated with the image impedance theorem that
the low- and high-pass sections have one simple attenuation peak at the impedance con-
trolling frequency, and the band-pass sections have a geometrically symmetrical pair. It
is convenient to use a universal frequency variable, denoted by x, in the description of all
the sections. The definition of this variable for each type of filter is included in the figure.
For the low-pass sections, the pass band extends from x — 0 to +1, and the attenuation
band from x — -fl to plus infinity. For the high-pass sections, the pass band extends
from 2 = 0 to 2;= —1, and the attenuation band from x = —1 to minus infinity. For
the band-pass sections, the pass band extends from x — — lio x = +1 with the mid-band
at x = 0; the attenuation band above the upper cutoff extends from x = +1 to plus
infinity, while the attenuation band below the lower cutoff extends from x = — 1 to minus
infinity.
TJNSYMMETRICAL SECTIONS
6-51
i
ii
^_L UftJ
+
+
e i
-i—4-
Lo£Qj
H-
J I
3
5
'T
ii
a I
^aS"-.
-Ill6*
a*".g
6-52
PASSIVE CIRCUIT ELEMENTS
Mh_
ioooJ
1
— \WL> — 1| —
1
O
HI
I
p «
rf co f
A bO c
ill
J<
I
•s
eg
I
a
1
I
I
UNSYMMETRICAL SECTIONS
6-53
The choice of a particular value of the parameter m is dictated by the image impedance
characteristic that is desired (on the assumption that the location of the associated atten-
uation peak is satisfactory). Several characteristics are shown in Fig. 15 including the
constant-/? type, for which m = 1.0. These curves exhibit the course of the mid-series
image impedance and the mid-shunt image admittance as a function of the frequency
variable, x. A generally satisfactory value of the parameter is m = 0.6. It is seen that
the image impedance of this section remains within about 4 per cent of a constant value
over 87 per cent of the pass band. The actual impedance measured at the terminals of
1.2
1.1
1.0
0.9
0.8
0.7
I 1 0-6
II 0.5
IJL
0.4
0.3
0.2
0.1
V
~0 0.1 0.2 0.3 0.4 0.5 0.6 0.7 0.8 0.9 1.0
Frequency Variable x
FIG. 15. Image Impedance Characteristics of Several m-derived Filter Sections
the filter is identical with the image impedance only if the other end of the filter is termi-
nated in the image impedance at that end. A general formula for computing this im-
pedance is
where Zj is the image impedance at the end of the filter for which the driving point im-
pedance Z is being calculated; Z/2 is the image impedance at the far end which is termi-
nated by the load impedance Rt', and 6 is the total image transfer constant of the complete
filter. Evidently, if Z/2 = Rt, then Z = Z/r
TWO-FREQUENCY CONTROL SECTIONS. Terminating sections which present
an image impedance having two controlling frequencies may be derived in a number of
ways and exist in various forms. The sections listed in Fig. 16 serve as a direct transition
from a constant-X image impedance to a "two-frequency control" image impedance.
They are units consisting of four branches which cannot be separated at any internal
junction, even though they have the structural appearance of 1 1/2 section m-derived
filters. The low- and high-pass sections have two simple attenuation peaks, and the
band-pass have two geometrically symmetrical pairs of simple peaks. The behavior of
6-54
PASSIVE CIRCUIT ELEMENTS
i
•ss
III
o^
UNSYMMETRICAL SECTIONS
6-55
tf
i"B
g g
+
'5
g
A
S
§
1
I
>
Ci
JfS
>SVVs
V 8
P
S
EH
^
2
Q
«5
6-56
PASSIVE CIBCUTT ELEMENTS
the image impedance depends on the choice of the parameters, mi and mz. Since the usual
objective is to obtain an impedance which approximates closely to a constant resistance,
these parameters may be determined most easily by the method described in the next
section.
25. TCHEBYCHEFF TYPE CHARACTERISTICS
In the preceding two sections, attention has been directed at the building blocks that
make up a composite filter. These elementary units can be assembled to give a great
variety of characteristics. The characteristics desired in a filter design depend, of course,
on the particular use for which the filter is intended. Many applications include the re-
quirement that the image impedance should be substantially constant over a prescribed
portion of the pass band. Another frequent specification is that the attenuation exceed a
given value at all frequencies more than a certain distance beyond the cutoff. An equiva-
lent statement of these requirements is: (1) the image impedance function, Zj/Rt, should
approximate to unity over a pre-
assigned interval of the pass
band; (2) the image transfer func-
tion, tanh 6, should approximate
to unity over a preassigned inter-
val of the attenuating band.
A desirable approximation is
one for which the maximum de-
partures of the function from
unity are the minimum. This is
known as the Tchebycheff: ap-
proximation, proposed originally
by W. Cauer for this application.
In this type of approximation,
as illustrated in Fig. 17, the func-
Scale for 2T/R< or Rf/Z].
Scale for tanh 0/2 or coth 0/2
l»i
--
-, — -7- for low-pass filter
Jc
x = — 7 for high-pass filter
-
~ /l)
r band-pass filter
FIG. 17. The Tchebycheff Type of Approximation to a Con-
stant Value
tion winds about unity in such a
way that all the maximum values
(U) are equal, and all the mini-
mum values (I/ (7) are also equal.
Unity is the geometric mean of
the maximum and minimum val-
ues. The number of intersec-
tions with unity is determined by
the degree of the function.
ATTENUATION CHARACTERISTIC. The image transfer function, tanh (6/2}, of a
symmetrical filter is written in terms of the frequency variable, \/x. The critical frequen-
cies and the constant multiplier are so chosen that the function is constrained to lie between
the limits U and 1/Z7, in the frequency range from l/k to infinity, as shown in Fig. 17.
The intersections with unity correspond to peaks of infinite attenuation; the equal values
of minimum attenuation, AQ, are equal either to 2 arg tanh U, or 2 arg coth U. For a
given number of filter sections, there is a definite relation between k and AQ.
This relation is presented in chart form in Fig. 18. The parameter, JV, is equal to the
number of transfer constant controlling factors in the image transfer function. The
number of m-derived low- and high-pass filter sections, Figs. 8 and 9, is equal to (N -f- 1) ;
the number of m-derived band-pass sections, Figs. 10a and 106, is [2(N -f- 1)]. The
horizontal scale of this chart is spread out considerably for values of k near unity by using
the variable a defined by the equation k = sin a. The data required for making up this
chart may be obtained from the following set of computations:
(1)
(2)
(3)
(4)
a = arc sin k
1 -
2e
AQ ± 20(N + 1) log- -6.0
Q.
(in db)
This relation, derived by S. Darlington, gives a result good to within 0.1 db provided AQ
is greater than about 6 db. A table of log q vs. a. is contained in Funktionentafeln by
Jahnke and Emde. This may be used in place of (2) and (3) .
TCHEBYCHEFF TYPE CHARACTERISTICS
6-57
It is not likely that arbitrarily chosen values of AQ and a will lie on one of the curves.
Thus, a compromise must be made between minimum attenuation and the interval of
the attenuating band that is covered. For example, if a filter is to be designed to attenuate
frequencies above x = 1.10 by about 60 db, a choice must be made among the possibili-
ties: A0 = 52 db, a = 65°, I/A = 1.10, A" = 2; AQ = 60 db, a = 58°, l/k = 1.18, N = 2;
100
90
80;
<60
<
E40
20
10
\
N
X'h
K
0.01
0.05
0.1
0.2 -5
20.0
50° 55°
60° 65° 70°
a=arc sin k
75° 80° 85"
FIG. 18. Design Chart for Determining the Number, N, of Frequency Control Factors Required for
a Specified Reflection Coefficient or Minimum Attenuation
AQ — 60 db, a = 73°, l/k = 1.045, N =3. It is customary to design to a value of min-
imum attenuation which is 6 db greater than the desired minimum insertion loss. This
allows for 3 db reflection gain at each end of the filter, which is the maximum value that
may be realized.
The design formulas for the element values are expressed in terms of the impedance level,
R, the cutoff frequency or frequencies, and the parameter, m. At this point it is assumed
that the first two quantities are known. The values of m are determined from the fre-
quencies of infinite attenuation. They are given by:
s - 1, 2, ••-, A"+ 1
where sn denotes an elliptic sine function of modulus k, and K is the complete elliptic
integral of the first kind. Each choice of the index s specifies an attenuation peak at the
frequency corresponding to xs.
The evaluation of the sn function can be performed by means of elliptic integral tables.
However, a preferred method is to use the approximation:
ur
r J
where
2u ••
1 - VJfc
1 + Vk
2s - 1
2(A^ -f 1)
= 1, 2, ••-
6-58 PASSIVE CIRCUIT ELEMENTS
The actual peak frequencies used in the definition of m in Figs. 8, 9, 10 are obtained
from the normalized frequency for each type of niter from the following relations:
(a) low-pass /w = fcxs
f
(6) high-pass fw — —
(c) band-pass /« - fn[Dx, + Vl + (Da;,)2]; (>/2)
/_ = fm[-Dx, + Vl + (Dxsn ( <A)
D=f±^
The band-pass attenuation characteristic is geometrically symmetrical about the mid-
band frequency. That is, the attenuation at a frequency, fx, above the upper cutoff is
the same as the attenuation at the frequency /_» = fm2/fx below the lower cutoff. Instead
of designing the four-element band-pass sections, Fig. 10, it is more convenient and
economical to use the six-element sections described in Fig. 14. Two half-sections must
be joined together to realize the performance predicted by the above design method. It
is to be noted that the parameter, m, is expressed directly in terms of xs.
IMAGE IMPEDANCE CHARACTERISTIC. The image impedance function is written
in the form Zi/Rt in terms of the frequency variable x. The terminating resistance is
denoted by Rt- The critical frequencies and the constant multiplier R are chosen in such
a way that the function remains within the limits U = R and \/U = 1/R over the fre-
quency range from zero to k, as shown in Fig. 17. Perfect match points correspond to the
intersections with unity. Because of the reciprocal nature of the departures from unity,
it is evident that the maximum departures of the magnitude of the reflection coefficient
from zero are all equal over the approximation interval.
The relation between the reflection coefficient, p, and the pass-band interval, &, within
which the reflection coefficient does not exceed the prescribed limit is presented in Fig. 18.
(The scale chosen for the reflection coefficient is not a convenient one. However, it can
be easily transformed into the db scale in accordance with the relation AQ = 20 log
(100/p), where p is in per cent, and AQ in decibels.) The parameter N is equal to the
number of impedance controlling factors in the expression for the image impedance. For
the constant-X sections, Fig. 13, N — 0; for the usual m-derived sections, Fig. 14, N = 1;
and for the "two-control" terminating sections shown in Fig. 16, N = 2.
The element values for the terminating sections depend on the cutoff frequencies, the
impedance level, and the parameter m. It is assumed here that the cutoff frequencies
are known. The impedance level is specified by:
R_ = 1 + p 1 - p
Rt ~ 1 - P °r 1 + P
where Rt is the terminating, or load, resistance, and p is the absolute value of the reflection
coefficient (not in per cent). The first relation is used, for a mid-series type impedance
when N is even, and for a mid-shunt type when N is odd; the second relation is used for
the other two possibilities.
The values for m are determined in terms of the frequencies of infinite attenuation.
These are specified by:
i / +TT \
t = 1, 2, --,N
The following approximation is usually more satisfactory for evaluating these peak fre-
quencies than the use of a table:
xt Vfcl + uv + u?~v
where
1 - Vk
2u = - —
1 + Vfc
and
TCHEBYCHEFF TYPE CHAKACTEEISTICS
6-59
V
1
\
I
E
qp'uoijsnusuv
2 °3
qp 'u
6-60
PASSIVE CIRCUIT ELEMENTS
T
c -
'c o
P 0>
\
II
I—
1
g
•qp 'u
- ID
rH
10
o
S
6
MAYER'S THEOREM 6-61
Illustration. The application of this techniaue to the design of a band-pass filter serves to clarify
some of the details of the procedure. It is assumed that the lower cutoff is 12 kc and the upper cutoff
is 16 kc. The minimum insertion loss should be at least 52 db above 16.4 kc, and below 11.6 kc. The
reflection coefficient should be less than 1 per cent between 12.1 and 15.9 kc.
The terminating sections are designed first, so that the attenuation which they contribute may be
deducted from the 58 db requirement (allowing 6 db for reflection gain). From the curve, X — 2, on
Fig. 18, it is seen that a 1 per cent reflection coefficient can be realized over the portion of the pass
band corresponding to a — 76° by using the sections shown in Fig. 16. The actual frequency range
lies between the limits /+ = 15,931 and /_= 12,050 corresponding to a; = k = sin 76° = 0.9703, as
computed from:
The plus sign gives the frequency above mid-band, and the minus sign the frequency below mid-band.
The quantity D is the relative bandwidth equal to Cfc — fi)/2fm. The distance between the upper
and lower frequencies is proportional to the absolute band width, i.e., (/+ — /_) — (fz ~~ /i)x.
The impedance level of the section, for p = 0.01, is found to be R = 1.020.Kf. For precise results, a
value for the reflection coefficient, superior to that read from Fig. 18, may be calculated from the equa-
tion p — Sq . The image impedance characteristic is similar to the curve displayed in Fig. 17 with
U = 1.020 and k — 0.9703. The negative half extending from zero to minus one, corresponding to the
interval from mid-band to the lower cutoff, is a duplicate of the part shown.
The final step in the design is the evaluation of the peak frequencies by means of the approximation
given above, with the index r = 1/3 and 2/3. The results are xi = 1.0351 and x% = 1.3484; the corre-
sponding values of the parameter are mi = 0.25838 and mz = 0.67082. The element values are ob-
tained from Fig. 16. An appropriate configuration is shown in Fig. 19a, as well as the attenuation
characteristic of the two terminating sections, which is obtained by doubling the result calculated
from the formula in Fig. 16.
That part of the complete filter which is between the terminating sections supplies the balance of
the required attenuation, i.e., the difference between 58 db and that shown in Fig. 19o. This unit may
be designed by fitting together the attenuation characteristics of four m-derived sections (Fig. 10) ;
several trials may be necessary. It is interesting to see how the design process under discussion leads
directly to a satisfactory choice for these intermediate sections.
The chart, Fig. 18, is entered with AQ = 58 db. This attenuation can be obtained with three sections
at frequencies above and below those corresponding to a = 60°. The limits are found to be f+ = 16,357
and /_ = 1 1 ,738. The values for the peak frequencies are computed from the approximation given above,
with the index r = 1/6, 3/6, 5/6- They are x\ = 1.1742, and xi = 1.4142, and xz = 3.333; the corre-
sponding values of the parameter are mi = 0.52415, and mi — 0.70711, and 7713 = 0.95393. The
attenuation characteristics of the three sections are calculated from the formula given in Fig. 14 (this
formula applies to a half -section so that the result must be doubled). Figure 196 is a sketch of the
complete characteristic. Two of the possible configurations are shown; the first consists of sections
chosen from Fig. 10, and the second is taken from Fig. 14 (an equivalent shunt branch is used).
The sum of the characteristics, Figs. 19a and &, is far in excess of the attenuation required. It is
observed that the terminating section has a peak at £2 — 1.35. This is close to the peak, x» = 1.41, of
one of the attenuation sections. Consequently, this latter section may be omitted from the intermediate
part of the complete filter without affecting greatly the minimum attenuation of 58 db. There is a
considerable increase in attenuation between the cutoffs and the limit frequencies, ±1 /k, owing to the
first peak in the terminating sections. However, a large part of this surplus will be lost because of
dissipation in the components. The overall attenuation is plotted on an arc sin frequency scale in Fig. 19c.
26. MAYER'S THEOREM
The effect of uniform dissipation in the elements on the characteristics of a reactive net-
work can be estimated readily by means of Mayer's theorem. This states that:
A and B represent the real and imaginary parts, respectively, of a network characteristic
in the absence of dissipation. Ad and Bd are the corresponding quantities when dissipation
is present. As usual, <a is 2ir times the frequency. The average dissipation is:
Q 2\QL Qc)
where Qz, is the average aL/r for the coils, and Qc is the average eaC/g for the condensers.
Frequently, the condensers are considered relatively non-dissipative, so that Q = 2Q&.
Since these relations come from a Taylor's series development of the network function,
they are usable only in the regions where the function is well behaved. For example, if
A and B represent image attenuation and image phase shift, the approximation fails in
6-62 PASSIVE CIRCUIT ELEMENTS
the neighborhood of the cutoffs and the attenuation peaks; on the other hand, if A and B
represent the insertion loss and insertion phase shift, the approximation holds everywhere
except near the loss peaks; a similar remark obtains for driving point impedance, current
ratio, voltage ratio, etc., functions.
These formulas lead to some useful general conclusions. They indicate that, to a first
approximation, the change produced in the real component of a network characteristic by
dissipation is proportional to the slope of its imaginary component, and vice versa. It is
particularly interesting to note the effect in respect to characteristics which approach the
ideal. For example, the approximation to an ideal filter is designed to have a constant
(zero) attenuation and a phase shift which varies linearly with frequency over most of the
pass band. It is to be expected that the phase characteristic will be changed very little
by dissipation since the slope of the attenuation is zero. On the other hand, the attenua-
tion characteristic will be affected when dissipation is present. However, over the fre-
quency range for which Q is proportional to frequency, the attenuation will be constant
and proportional to the phase slope. Consequently, the filter introduces a flat loss but
does not introduce distortion.
REFERENCEvS
Bartlett, A. C., The Theory of Electrical Artificial Lines and Filters. John Wiley (1930).
Bode, H. W., A General Theory of Electric Wave Filters, J. Math, and Phys.t Vol. 13, 275-362
(November 1934).
Bode, H. W., and R. L. Dietzold, Ideal Wave Filters, B.S.T.J., Vol. 14, 215-252 (April 1935).
Cauer, W., Siebschaltungen, V.D.I. Verlag G.m.b.H., Berlin (1931).
Cauer, W., New Theory and Design'of Wave Filters, Physics, Vol. 2, 242 (April 1932).
Darlington, S., Synthesis of Reactance 4-Poles, /. Math, and Phys., Vol. 18, 257-353 (September 1939).
Foster, R. M., A Reactance Theorem, B.S.T.J., Vol. 3, 259-267 (April 1924).
Guillemin, E. A., Communication Networks, Vol. II. John Wiley (1935).
Zobel, O. J., Theory and Design of Uniform and Composite Electric Wave Filters, B.S.T.J., Vol. 2,
1-46 (January 1923).
RADIO ANTENNAS
By J. C. Schelleng *
GENERAL FUNCTION AND DESCRIPTION. The antenna is the means of coupling
between the medium of propagation and the transmitter or receiver. Its purpose is to
convert power into outgoing electromagnetic waves, or to extract power from incoming
waves. These two processes are reciprocal, but other factors such as discrimination against
static introduce new requirements which differentiate a good transmitting from a good
receiving antenna.
Not only should an antenna be an efficient converter between radiant and guided
energy, but it should also be most effective in the direction of the station with which it is
communicating. At the receiving end, directivity performs two useful functions. The
first is that of impressing on the early stages of the receiver a relatively intense signal so
as to override the inherent circuit or tube noises. The second and often the more important
is that of discriminating against electrical disturbances in the medium, such as atmospheric
noise, thereby increasing the ratio between signal and noise components. If the atmos-
pherics should arrive from the direction of the signal, then, of course, no advantage would
result from this means. When, on the average, they arrive with equal intensity from all
directions, the advantage is considerable. If it happens, as in communication between
Europe and America, that a very small part of the total noise arrives from the direction
of the desired signal, a very great advantage is realized. Indeed, because of their ability
to discriminate against atmospherics arriving from the rear, it is sometimes the practice
to use as receiving antennas devices that would ordinarily be relatively poor radiators.
Practical antennas differ widely. Perhaps the simplest is a straight vertical wire as
shown in Fig. la, 6, c, and d. For the lowest frequencies used in radio the length is a very
small fraction of a wavelength, but with higher frequencies the vertical wire may exceed a
half-wavelength. The dotted lines indicate roughly the distribution of current. Several
antennas may be arranged to form a directive array as shown in Fig. H. An antenna
one-half wave long (Fig. Ig) is known as a half-wave linear antenna.
When the frequency is low (long waves) , the antenna may take the form of an L or a T,
a hundred or so feet high and several hundred long (see Fig. le and /). The horizontal
portion is known as the flat-top, the vertical as the lead-in. Frequently a large coil of wire
is used as an aerial as shown in Fig. Ik. It is known as a loop.
* In this revision a considerable amount of material from the article Radio Antennas (7-57) appearing
in the 1936 Edition of the Pender-Mcllwain Handbook, and written by G. C. Southworth, has been used.
KADIO ANTENNAS
6-63
In the highest decade of the radio spectrum (in 1949 the practical limit seems to be of
the order of 30,000 megacycles per second, wavelength 1 cm), the low-frequency technique
associated with radiation "from the outside" of the conductors has become relatively
Grounded Antennas
Ungrounded Antenna
Ungrounded Antennas Without Loading With Loading Loop Antenna
L <y)/=5>\ m7=—
Broadside Acray
0
I")
FIG. 1. Representative Forms of Antennas
Sidp ~*'2~'
Elevation Front E!evat!on
Y\\i aim IK,
in ji i i IN iHf
difficult owing to the small size of the wavelength, and antenna designers tend to draw their
inspiration from wave-guide principles and from optics. Typical antennas now are found
to employ wave-guide apertures or horns, parabolic reflectors or lenses, as well as many
(a)
FIG. 2. Forms of Quasi-optical Antenna
of the older techniques. Figure 2a illustrates radiation from the open end of a circular
wave guide, 2b shows a pyramidal horn formed by tapering from a small rectangular wave
guide, and 2c shows a linear half-wave antenna at the focus of a paraboloidal antenna.
6-64 PASSIVE CIRCUIT ELEMENTS
CLASSIFICATION. Table 1 is an attempt to classify the many diverse forms of
antennas which have found use. Ignoring distinctions between transmitting and receiving,
it gives one type of classification based on general form rather than specific application.
In spite of a degree of artificiality it covers most of the common types. The relatively
non-directional appear early in the list; the highly directional are found at the end.
Table 1. Classification of Antennas
Linear Conductor Antennas
L, T, umbrella, multiple-tuned electric dipoles, "vertical radiators," whip, trailing- wire, vertical
wire, horizontal wire, wave antenna, loops, etc.
Wave-guide Antennas
Small wave-guide apertures:
Open-end wave guide.
Slot antennas.
Various reflector or lens feeds, etc.
Large wave-guide apertures: Horns.
Dielectric antennas: Polyrods.
Quasi-optical Devices: Antennas Using Reflectors or Lenses for Collimating
Spherical optics: Point sources ("dipoles" or wave-guide apertures) in conjunction with spherical
reflectors or lenses.
Cylindrical optics: Line sources (arrays, reflectors, lenses) in conjunction with cylindrical
reflectors or lenses.
Arrays or Combinations of Above Devices
Long-wire antennas.
Wave antenna.
V-antenna.
Rhombic antenna, etc.
Linear arrays.
Broadside array.
End-fire array.
Fishbone.
Musa.
Turnstile.
Clover leaf, etc.
Curtain arrays.
Franklin.
Pine-tree.
Chireix-Mesny.
Sterba.
Arrays of: Horns; quasi-optical devices; wave-guide apertures.
RADIATION, ABSORPTION, AND RECIPROCITY. In general, the radiation from
an antenna can be calculated if the tangential magnetic and electric fields subsisting over
any closed surface containing the antenna are known. The tangential magnetic field
measures linear density of an equivalent electric current in the surface at right angles to
the tangential field; likewise the tangential electric field measures a linear density of
"magnetic current." General formulas (beyond the scope of this article) exist for calculat-
ing from these the radiated field (S. A. Schelkunoff, Reference 1, 9.1-7, 9.1-9 and 9.1-10).
They are necessary, for example, in calculating the radiation from an electromagnetic
horn. In many other cases, including practically all antennas of older types where the
energy prior to radiation was guided near the outside of conductors rather than through
hollow guides, this procedure simplifies: the closed surface now may be taken as the surface
of the conductor of the antenna itself and the electric currents of the equivalent sheet
become the usual antenna currents, while the "magnetic currents" become zero owing to
the disappearance of a tangential electric field at the surface of the conductor. The fact
that in the lower-frequency ranges the electric current in conductors can be conveniently
measured by ammeters gives a special importance in those ranges to formulas in which
the antenna current is assumed to be known.
An analogous process occurs in reception, in which equations might be set up for inte-
grating the total effect on the receiver due to the electric and magnetic distributions over
a closed surface containing the antenna, but, since these fields are in part reradiation
associated with the response of the receiving antenna, the problem is more involved than
that of the transmitting antenna and it is common to invoke the law of reciprocity instead. .
As applied to radio wave propagation through a simple linear medium (excluding non-
linear circuit elements and the ionosphere), this law says that, if there is a single zero-
impedance generator in the transmitter and a zero-impedance ammeter in the receiver,
the generator and the ammeter may be interchanged without affecting the current
measured. An alternative expression of the law is : if a constant-current generator in the
transmitter produces a reading in an infinite-impedance voltmeter in the receiver, the
generator and the voltmeter may be interchanged without affecting the reading. These
PRINCIPLES OF LINEAR CONDUCTOR ANTENNAS 6-65
statements say nothing explicitly about the power transfer, but the following one does: if
the internal resistance R of a generator having zero reactance is matched to the trans-
mitting antenna, and if the receiving antenna is matched to a load whose impedance is R,
then the power transfer will not be affected by interchanging the generator and the load.
It follows from any of these statements that a given antenna has the same directional pattern
for receiving as for transmitting.
27. PRINCIPLES OF LINEAR CONDUCTOR ANTENNAS
What takes place in even a simple transmitting antenna is a matter of such great com-
plexity that a rigorous description is beyond the scope of this article; nevertheless it will
be well to recognize the nature of the problem. One aspect of it is the calculation of
external fields, assuming a knowledge of the distribution of current in the conductors.
Feeders all excited In same phase
(a) Sterba array
ParasifTc
'radiator
To transmitter
(5) Chireix-Mesney array
Feeders all excited In same phase
(e) Pine Tree arrays
th+4 t
f
t t
t
t] 1
*
fc
t
> {g {s js
IB is £ t
t
ll t
t
1
1
t| t
4
FtankFin arrays
To transmitter
(/) RCA Broadside arrays
FIG. 3. Typical Antenna Arrays
This problem is completely solved by integrating for each point in space the retarded
effects of currents at different parts of the antenna. To the extent that we are satisfied
with the assumed current distribution, a satisfactorily complete formal solution is always
possible. Many results of great engineering usefulness have been so obtained; the usual
assumption is that the current is distributed sinusoidally, that the standing-wave pattern
is formed by equal waves traveling oppositely with the velocity of light (3 X 10s meters
per second) , with current nodes at open ends of conductors. This means that the standing
wave will have minima at intervals of one-half wave, with maxima at intermediate points,
the instantaneous current being oppositely directed either side of a minimum, as shown
in Fig. Id, Ik, and \i. In certain problems it is convenient to regard the radiation as
issuing from certain centers, such as the midpoint or maximum between adjacent minima.
On this view a small radiator may have a center of radiation much as an extended body
has a center of mass. For sections of conductor whose length is small compared with a
wavelength the current distribution may be substantially uniform, as in the vertical lead
of a large flat-top antenna, or in a loop small compared with a wavelength. There is a
considerable field where the engineer may employ this concept without apology to the
mathematician .
There are other cases where he needs to watch his step carefully, as for example in the
antenna shown in Fig. Za where for qualitative purposes the standing wave is shown along
6-66
PASSIVE CIRCUIT ELEMENTS
the folds of the wire. The existence of current minima in this antenna was checked
experimentally by E. J. Sterba, but he found that, as the antenna was extended by adding
more sections at the top, the
(1) (2) (3) (4) (5) (6) (7) lower minima became less
definite and ceased to be nulls.
This is an extreme case per-
haps beyond mathematical
solution, but it illustrates the
matter.
A second aspect of this the-
oretical problem is the actual
determination of the currents
and voltages that exist on an
antenna having specified the
applied or external forces.
S. A. Schelkunoff has given
a general theory of certain
forms of antenna which is
JL
2
Characteristic
impedance
FIG.
equa:
cert
.
antenna of any shape is similarly represented, except that the char-
acteristic impedance is variable.
ftrfq;T1orv trfln*mi««irm linoc
ordinary transmission lines,
the distribution of a linear
charge density is the same as
that of voltage, but this is not generally true in antennas. The explanation is that antennas,
unlike ordinary transmission lines, support more than one mode of propagation. As far as
.10000
8000
6000
4000
2000
.1000
J 80°
° 600
8 400
03
.S2
"t/1
2 200
D
Q.
_C
100
80
60
40
20
10
y soo
600
0.20
0,25
0.30
0.35
0.40
0.45
0.50
FIG. 5. The Input Resistance of Hollow Cylindrical Antennas in Free Space. For vertical antennas
over a perfectly conducting ground divide the ordinates and Ka by 2.
the current associated with the principal mode is concerned (the mode that we are think-
ing of when we draw the oversimplified current-distribution curves which we have just
PRINCIPLES OF LINEAR CONDUCTOR ANTENNAS 6-67
been discussing), radiation is strictly an end effect: "It is permissible to think that a wave
emerging from a generator in the center of an antenna is guided by the antenna until it
reaches its boundary sphere passing through the ends of the antenna and separating the
antenna region from external space; at the boundary sphere some energy passes into ex-
ternal space and some is reflected back — a situation existing at the juncture between two
transmission lines with different characteristic impedances." This will be clearer by ref-
erence to Fig. 4, taken from Schelkunoff, where the "antenna region"1 or -sphere is re-
placed by a transmission line having length equal that of the antenna, the line having
appropriate characteristic impedance K and terminating impedance Z*. The legend makes
the figure self-explanatory.
0.45
0.50
FIG. 6. The Input Reactance of Hollow Cylindrical Antennas in Free Space. For vertical antennas
over a perfectly conducting ground divide the ordinates and Ka by 2.
The input resistance and reactance of perfectly conducting cylindrical antennas in free
space as given by Schelkunoff are plotted in Figs. 5 and 6, the parameter Ka, the char-
acteristic impedance, being given in Fig. 7. These curves were obtained on the assumption
that the current flowing over the edge at the top of the antenna is zero. For Ka < 700
there is a small current over the edge which, if included in the calculations, would increase
the maxima of the input resistance and reactance by a small percentage. Note the points
where input reactance is zero, and the deviation of the lengths from 0.25X and 0.5X, as
found experimentally by C. R. Englund.
In some low-frequency antennas where radiation resistance is low, the input reactance
has often been calculated by regarding the antenna as a transmission line without resist-
ance, using the formula
X - - -yp cot (cozvz^Ji ) CD
where Li and Ci are inductance and capacitance per unit length, I the total length, and w
the angular frequency. Such a line is resonant when I = X/4, 3X/4, etc., and antiresonant
6-68
PASSIVE CIRCUIT ELEMENTS
when I — X/2, X, etc. If a lumped inductance is connected in series with the long antenna
assumed, resonance will occur when
coZ/ — Y — cot (ool v L/iCi ) — 0
The effect of capacitive loading may be found in a similar manner.
When an antenna of this kind does not exceed a quarter-wave in length it may be roughly
considered part of a resonant circuit made up of lumped inductance and capacitance as
1400
1000
800
600
200
1000
I/a
10,000
100,000
FIG. 7. The Average Characteristic Impedance: (1) Cylindrical Antenna, (2) Spheroidal Antenna,
(3) Antenna of Rhombic Cross-section. I is the length from middle of antenna to the ends; a is the
maximum radius of conductor.
follows: Le — ZLi/3 henrys and Ce = IC\ farads together with whatever loading may have
been added. The shorter the antenna the better is the approximation.
RESISTANCE OF ACTUAL ANTENNAS. Antenna resistance is the quotient of the
mean power supplied to the antenna divided by the mean square of the current referred
to a specified point of the antenna. It thus includes a component associated with the
useful radiation of power and others related to undesirable losses in the conductors,
ground, etc. Radiation resistance is thus
the quotient of the mean radiated power
divided by the mean square of the cur-
rent referred to the specified point, and
radiation efficiency is the ratio of radia-
tion resistance to total resistance.
Figure 8 shows the general way in
which radiation resistance, with the
losses in the ground and in the conduc-
tors, varies with frequency. An efficient
antenna being "one in which radiation
resistance predominates, the desirable
operating range is well to the right in
the figure. At the lowest of radio fre-
quencies, however, economic factors
makes high efficiencies unrealizable, and
efficiencies of a few per cent, or less,
are representative. In the example
shown in Fig. 8, the wire resistance is
substantially independent of frequency,
but in general this is not true.
The radiation resistance of a straight vertical wire of infinitesimal diameter referred to
the point where it connects through a coupling or load impedance to a perfect ground
varies from zero to 36.6 ohms as its length increases from zero to a quarter-wave (half
the value given in Fig. 5) . A convenient approximation for the radiation resistance pro-
vided that the actual height is well below X/4 is 1607r2A2/X2, where h is an effective vertical
length of the radiator and X is the wavelength in the same units. If, for example, we con-
Resistance - Ohms
i-» K> to 4* u
o o o o o c
|
, /
1
0
De'sirable
perating Rang
k-
e-j_
7~~
/
i
/
Y
i
j&
/
i
<^
^l«
/
\
i
^
^
?
$
k\
^
.
*$>
A
£>
\
\
\
^
\
X,
-C—
^
ll*
sisti
J«.
ofjw
\ros_
— - —
^.-~
ix.
— -
Groin
1.^
ssji
, —
—
) 25 50 75 100 125 15
Frequency • Kilocycles
FIG. 8. Components Which Go to Make TJp the Total
Resistance of a Simple Antenna
PRINCIPLES OF LINEAR CONDUCTOR ANTENNAS 6-69
sider a vertical wire A/4 long (which we have just stated is too long for this approximation),
the assumed sinusoidal current distribution makes h = 2/x - X/4 = A/2?r, and radiation
resistance of 40 ohms is indicated. Comparison with the correct value of 36.6 ohms
indicates that for antennas shorter than X/S the approximation will usually be acceptable.
When the operating frequency is low it is uneconomic to construct a vertical wire even
approaching a quarter-wave in length. Under these circumstances it is customary to
combine a rather large flat-top with a moderate vertical lead, in order to hold costs to
the minimum. This leads, however, to low radiation resistance and so requires that other
resistances be kept correspondingly low. Thus, if the radiation resistance should be as
low as 0.05 ohm, an elaborate counterpoise or other ground system would be necessary to
keep the losses within reasonable
bounds. Grounded antennas
ANTENNA IMAGES. A portion
of the wave radiated from an an-
tenna is "reflected" by the ear that
points some distance away. To an
observer located at a considerable
distance the total radiation appears
to be made up of two components,
one which arrives directly from the
antenna itself and the other which
appears to be coming from a virtual
antenna located below the surface
of the earth. The latter, sometimes
known as an image antenna, behaves
in different ways depending on the
soil adjacent to the antenna. Figure
9 pictures the relation between the
effective currents in real and image
antenna, assuming the earth to be
perfectly reflecting.
FIELDS ASSOCIATED WITH AN ANTENNA. The wave radiated from an antenna
appears as two fields, (1) an electric field 8 which may be measured in volts per meter,
and (2) a magnetic field which may be specified in amperes per meter. These components
are so inseparable as to be regarded as two aspects of the same thing. They are perpen-
dicular to each other and to the direction of wave propagation and at any point of observa-
tion are in the same phase, reaching zeros and maxima at the same time. For a funda-
mental discussion on this subject the reader is referred to Section 5, articles 26-28.
The electric field produced at a distance of a few wavelengths from an antenna may be
calculated by means of the general formula applying to an elemental doublet
FIG. 9. Images of Representative Forms of Antennas
^~/&I cos oj (t - -c
cos 8
(2)
where 8 = the field intensity of the wave measured in volts per meter; / cos (cot + 90°) =
current flowing in the wire in amperes; / = frequency of the current in cycles per second;
X — wavelength corresponding to frequency/; c«j = 2-jrf; t = time in seconds; d = distance
to the antenna in meters; c = velocity of light = 2.998 X 108 meters per second; 81 = the
elementary length of wire or doublet from which radiation takes place — it is measured in
the same units as X; and d = angle of elevation of point at which the field is desired meas-
ured relative to a plane perpendicular to the conductor 5L In the formulas in this section,
any other unit of length can be used, provided it is used consistently in 8, X, d, c, A, etc.
The meter, however, is preferred.
Equations for the fields radiated by antennas of various shapes, such as given just
below, are obtained by integrating the above doublet expression over the entire conductor
system, having due regard for the distribution of the current. The fields at great distances
from antennas are usually much less than those calculated by these formulas. (See
Section 10.)
The voltage induced in an incremental length of conducting wire by a passing wave may
be found by either of two methods. The one starting with the electric field of the wave is
used the more. That component of the length lying parallel to the electric vector in the
wave front is multiplied by 8 measured in volts per unit length to give the required emf.
This same voltage may also be derived from the simple dynamo concept of the number
of lines of magnetic force cut per second; it will be realized, however, that this is not an-
other component of induced voltage but merely another approach to the same one made
possible by the identities expressed by Maxwell's equations.
6-70 PASSIVE CIRCUIT ELEMENTS
The instantaneous radiated power flowing through each unit of area perpendicular to a
plane wave front may be calculated by the expression
P = 0.00265s2 watt per square meter (3)
(See also Sect. 3 art 28 eq. [16].)
If eq. (3) is used for calculating the power picked up by a single wire, it must be assumed
that power is absorbed from a section of the wave front extending to about a quarter of a
wavelength either side of the conductor.
The field intensity at a horizontal distance d from a vertical grounded wire, length h,
carrying a uniform current I is approximately
8 = - - volts per meter (4)
etc
This applies to the vertical lead to an antenna having a relatively large flat top, the antenna
being located over a perfectly conducting earth.
The corresponding value for a coil or loop located in free space and having dimensions
small compared with the wavelength is
e =* — —z — ANI volts per meter (5)
dc*
where N is the number of turns and A is the area in square meters.
The effective vertical length of a loop in free space is given by
2-rrAN
h — — - — meters (6)
A
The fie.d intensity for a simple vertical quarter-wave antenna grounded at its lower end is
approximately
60/
e — — - volts per meter (7)
a
The effective vertical length of a grounded-quarter-wave antenna is
h = — - meters (8)
2iTT
In all these cases the current is to be measured at the point in the antenna where this
quantity is a maximum.
For formulas for field strength in terms of radiated power, see Section 10, Articles 20-24
of this handbook.
Figure 10 gives the directional diagram of a simple electric or magnetic radiating ele-
ment (a short wire or a small loop). It is worth noting that the same diagram applies
to both.
Axis of magnetic or
electric radiating element
I
^y^\
/ v/
\
i _ Equatorial plane
~' of elements
I
FIG. 10. Directional Diagram of Electric and Magnetic Dipoles. The length of the vector V is pro-
portional to signal intensity.
The directional diagrams for both the quarter-wave and half-wave antennas as well
as for an antenna 0.62 wavelength long are given in Fig. 11. It is to be noted that for this
latter a pronounced spurious lobe is formed. This continues to grow as the antenna is
further lengthened, thereby leading to a considerable amount of high-angle radiation and
possibly also to fading. The field laid down in the horizontal direction is for a given power
calculated to be a maximum when the length of the antenna is about 0.62 wave. (See
PRINCIPLES OF DIRECTIVITY
6-71
reference 2.) The half-wave antenna together with its earth image is roughly equivalent
to two collinear equiphased radiators and therefore is a special case of arrays discussed
below. Antennas a half-wave or so long have become widely used in broadcasting. See
"Antennas for Medium-frequency Broadcasting," article 31.
FIG. 11. Vertical Plane Directional Diagram of a Single Vertical Antenna of Various Lengths. (Only
one-half of the total vertical section is shown.)
28. PRINCIPLES OF DIRECTIVITY
An antenna which radiates or receives with uniform efficiency within a range of direc-
tion is said to be non-directional within those limits; when it favors a given direction, on
the other hand, it is directional. Thus, a vertical wire is non-directional in azimuth,
though it is directional in elevation. Ignoring non-coherent radiation, such as light, it
may be said that, for pure sinusoidal currents, a completely non-directional antenna does
not exist. It is, however, a useful concept to define the directivity of actual antennas in
terms of this imaginary non-directional source. Thus, the absoltite gain is commonly
defined as
0-£t (9)
where P is the power flow per unit area in the plane linearly polarized wave which the
antenna causes in a distant region (usually in the direction of maximum radiation), and
PO is the power flow per unit area which would have been produced if all the power had
been radiated equally in all directions. Where gain is referred to any other standard, it
will be specifically mentioned.
One special form of radiator, the current element short in comparison with a half-wave,
has frequently been used for reference in discussing directivity. It is, in fact, as non-
directional as a simple radiator can be. Actually, however, it has a power gain of 1.5 over
the standard described in the preceding paragraph.
6-72 PASSIVE CIRCUIT ELEMENTS
Though considerable directivity can at least in theory be accomplished with an antenna
whose largest dimension is small compared with one wavelength, it is not far from the
truth to say that all practical high-gain antennas depend primarily on having current
distributed over dimensions of several wavelengths. This statement applies both to
linear-conductor antennas and to quasi-optical devices.
The requirements of directivity are various. It may be necessary to limit antenna
effectiveness to a certain azimuth, to a certain elevation, or to both. A narrow beam may
be required in azimuth coupled with a wider one in elevation, as in some transatlantic
antennas used in the range of high frequencies; or a relatively sharp beam may be wanted
in elevation with little or no directivity in azimuth, as in television broadcasting; or
sharpness may be needed in azimuth with a specified variation of intensity in elevation,
as in the "cosecant" antennas of radar, etc.
The special distribution of current needed for directivity may be provided by arrays
of similar smaller radiating elements or by combinations of dissimilar elements. These
building blocks may be half-wave wires, loops, fiat-top antennas, and so forth. The dis-
tribution may be continuous: for example, an electromagnetic horn may be thought of
as an array of an infinite number of infinitesimal radiators.
An almost unlimited number of combinations is possible, since the directive effects
produced depend not only on the relative positions and spacings of the various units but
also on the amplitudes and phases of their currents as well. (See reference 3.)
Perhaps the best-known arrangement is that of a number of identical parallel antennas
arrayed laterally along a straight line. Usually the element antennas carry equal in-
phase currents. This produces the strongest signal in a direction perpendicular to the
line of the array and is thus known as a broadside array. An example is shown in Fig. 11,
above. In some cases the phasing of the currents is progressively delayed from antenna
to antenna to correspond exactly with the delay in that direction due to finite wave
velocity. Such an antenna is called an end-fire array because the radiation is most intense
along the line of the array.
EFFECTIVE AREA OF ANTENNAS. A wave incident upon a receiving antenna may
be thought of as a stream of energy possessing a certain power per unit of cross-sectional
area. If the receiver load is coupled to the antenna so as to abstract the maximum power
available, then the ratio of this maximum power to the power incident on the antenna
per unit area is defined as the effective area of the receiving antenna. A somewhat over-
simplified view is that the antenna presents this area to the energy stream and canalizes
the corresponding power flow into the receiver. An excellent treatment of relations to
be discussed in this section will be found in an article by H. T. Friis and W. D. Lewis.
(See reference 4.)
The effective area of a receiving antenna being by definition proportional to its power
gain, we may make the general statement that the ratio power-gain divided by effective
area has the same constant value for all antennas. Numerically it turns out that this
ratio is :
_ _
Eff.gain Aefl. X'
an important relation in antenna theory. It can be shown that it" has a useful interpreta-
tion in transmitting as well as in receiving: this same area then measures that broadside
"uniformly excited" area which would give the same transmitting gain as does the actual
transmitting antenna, the excitation being unidirectional (e.g., as when a reflector is used)
and the dimensions of the area being large compared with a wavelength. Hence, a lossless
transmitting antenna in which the radiation is associated with a large uniformly excited
area would, as a receiving antenna, make available to the receiver all the energy intercepted
by its actual area.
A very useful and simple free space transmission law (see reference 4) results by applica-
tion of these concepts to wave propagation between antennas of effective area AT and AR
(the subscripts refer to transmitter and receiver). The power delivered to the receiver
is then PR, which equals
Total power PT
- - - - - - —
- - - - - - - - — - - • • .efT. (recever) -A — 35 — ^
Area of sphere of radius d 47rcP X2
(receiver)
giving
The fact that the numerical constant turns out to be unity recommends this formula to
the memory.
DIRECTIVITY OF LINEAR CONDUCTOR ANTENNAS 6-73
Directional Diagrams
29. DIRECTIVITY OF LINEAR CONDUCTOR ANTENNAS
ARRAYS. Of the many directive patterns that may result from the various spacings
and phasings of two antennas, two are of especial interest. In the first the two sources
are separated in space by one-fourth of a wave-
length, and in phase by one-fourth of a period.
This arrangement, which is sometimes known
as a unidirectional couplet, gives a cardioid
pattern as shown in Fig. 12a, where the unit
antennas are vertical half-wave elements. As
compared with a single element it effects a
power gain of about 2 (3 db). In the other
arrangement the two elements are spaced one-
half wavelength and are driven in phase (see
Fig. 125). This also gives a theoretical gain of
about 2 (actually somewhat greater). The two
arrangements may be combined as in Fig. 12c
to give a total gain of 4 (6 db) . It is conven-
ient to regard the two antennas at the rear as
reflectors for those ahead. Directional effects
such as these are used practically not only to
increase signal in some desired direction but
also to ininimize its interfering effects in others.
Increased directivity may be obtained by
adding couplets to the arrangement shown in
Fig. 12c. The resulting increase is indicated
by Fig. 13. Although it is often most conven-
ient in practice to utilize spacings of one-half
wave in the array front, any spacing up to
about 3/4 wave may be used. For spacings
less than 0.6X it is the total length or aperture
of the broadside which is the important crite-
rion of gain, the gain variation due to spacing
being inappreciable. Figure 14 facilitates de-
termining the gain ratio of such arrays. The
aperture there referred to is about one-half
wave greater than the number of wavelengths
measured between extreme conductors of the
array. The reason for this rule is that the equivalent area of a thin wire properly coupled
to the terminal is finite (see paragraph following eq. [3]) .
When an array is formed by stacking similar units in tiers in the vertical direction,
added directivity is provided at some angle from the vertical, commonly at 90°, that is,
in the horizontal plane. The
units may, for example, be the
vertical elements previously
described, and if the elements
of a broadside array are so ar-
ranged the antenna resembles a
curtain. For vertical elements
the improvement obtained by
adding a small number of tiers
or stacks is less than that
achieved by the lateral arrange-
ment. (See reference 5.)
Simple but approximate
rules for unidirectional broad-
side arrays are as follows:
1. The gain ratio of a large
array of vertical couplets ex-
tending both laterally and ver-
tically (and including a reflect-
ing curtain) follows the general rule for gain G = 4^/X2 or, in terms of a short current
element as standard, G* = 8/3- x^L/X2 = 8.4A/X2, where the effective length is taken one-
half wave greater than the length between extreme conductors (see paragraph following
FIG. 12. Horizontal Directional Diagrams,
(a) Unidirectional couplet. (&) Two equi-
phased antennas spaced one-half wave-length.
(c) Two equiphased couplets.
120
100
o80
0
560
c
—
Arrangement of Array,
o o o o o o o o-i-
I
c
S
„
•-
z&
s
*•*
n
\
s
**
I
J
*'
s*
V
20
(
FIG.
s*
T
^,
--|
•-*
/>
*
^.
„-
s>
""
.--
+**•
^
s
^««
— -
--*
l£
^f
•y
D 4 8 12 16 20 24 28 32 36 4<
Number of Couplets
13. Variation of Directivity with Number of Couplets
Placed in Horizontal Array
6-74
PASSIVE CIRCUIT ELEMENTS
GQ- [3]), and the height as A/2 times the number of tiers or stacks. This assumes no ap-
preciable gap between tiers. For a single-tier antenna Gd = 10A/X2.
2. Doubling the length or the height, or adding the "reflector" curtain to the front
curtain, adds 3 db to the gain. Note the exception already indicated, however, that in
going from one to two tiers the increase is only about 2 db.
Arrays of this type have achieved considerable importance both in long-distance trans-
mission using short waves (high frequencies) and in medium-frequency broadcasting. In
the former use very considerable power gains have been employed, varying up to more
than 100. In the latter the gain has been valuable in extending coverage, but the most
important aim has been the suppression of signals in certain directions at night in order
to avoid interference with other
stations. Thus the directivity of
broadcast transmitting antennas
has two aims essentially corres-
ponding to those mentioned in the
first section with respect to direc-
tivity in reception, viz., increase of
signal and reduction of interfer-
ence.
The main problem in medium-
frequency broadcasting which leads
to the use of directional antennas
is the difficulty of giving local cov-
erage without causing interference
at distances of a few hundred to a
few thousand miles with other
transmitters using the same fre-
quency.^ This long-distance inter-
PIG. 14. Graph for Predicting Directivity of Arrays of Simple ference is propagated by reflection
80
a
g60
03
cr
I40
20
C
x
xl
^
X*
^
^x
^
^*
^
x^1
X
^
X
<S
) 2 4 6 8 10 12 1^
Aperture of Array,- Wave-Lengths
Half-wave Antennas. (Aperture is expressed in wavelengths
and is one-half wavelength greater than the horizontal dis-
tance between the extreme outside antennas.)
from the ionosphere, and therefore
not only azimuth but also elevation
must be considered. Regardless of
the height of the reflecting layer, the azimuth of waves between two points lies along the
great-circle path with considerable consistency, and an antenna which directs a minimum
of signal at all elevations in the vulnerable azimuth is usually the most desirable solution.
Sharp nulls in the elevational directive pattern are thus to be avoided if possible in view
of the variability in the heights of the reflecting layers. Often, however, a host of practical
considerations requires a compromise solution. (See reference 6.) Commonly, also, the
problem is complicated by the existence of more than one vulnerable direction. The
necessity of having the correct relative phases in the unit antennas has required the
development of techniques for controlling, measuring, and maintaining phases in practical
installations. (See reference 7.)
DIRECTIONAL CHARACTERISTICS OF LONG WIRES. When the length of a
wire carrying a high-frequency current is progressively increased, it breaks up into oscillat-
ing sections as was shown in Fig. K. This gives rise to radiation along certain preferred
directions in which in-phase components prevail. Figure 15 shows the directional patterns
for certain representative cases. It will be noted that the lobe designated as No. 1 ear
becomes progressively sharper and approaches the axis of the wire. At the same time
smaller lobes designated as No. 2, 3, and 4 ears are formed.
Several long wires each having characteristics of this kind may be so combined as to
give the arrangement as a whole very useful directional properties. In general, this is
accomplished by choosing arrangements that enhance the main lobe and at the same time
discourage the spurious lobes. The so-called tilted wire, folded wire, and rhombic antennas
are based on this principle. (See reference 8.)
EFFECTS OF SOIL AND TERRAIN ON DIRECTIVITY. The directive effects de-
scribed above assume that the array is divorced from any influence of the earth. In
practice, of course, this is not true. If the earth were perfectly conducting the array could
be so elevated as to make the image effect add to that of the array, thereby giving added
gain and a maximum intensity along the surface of the earth. These ideal conditions are
seldom attained in practice. At the frequencies at which directive antennas are most
used, there is a substantial refractive effect in addition to absorption that together tend
to distort the vertical directive characteristic.
Figure 16 shows the calculated directional distortion imposed by imperfectness of earth
conductivity on both a horizontal and a vertical receiving doublet for a representative
DIRECTIVITY OF LINEAR CONDUCTOR ANTENNAS 6-75
case. It is to be noted that the effect is less marked with a horizontal half-wave antenna
than with a vertical half-wave, and in both forms it is such as to cut down very materially
the intensities of waves along the horizontal. It fortunately happens that distant signals
Length"* X
Length =l|-X
No. 2 Ear
No. 1
Ear
No. 2 Ear No- I
No. 3 EarN \ Ear
No. 4 Ear,
No. 2 Ear, No. 1
No. 3 Ear> \ Ear
No. 4 Ear, / j /
Length=.2X Length = 5X Length -B\
FIG. 15. Directional Diagrams of Isolated Wires of Various Lengths
arrive at an appreciable angle above the horizon, so that such devices are still very effec-
tive. While this angle for transmission and reception of short waves may, for short
distances, be nearly 90°, for long distances it varies, say, from 30° for the lower frequencies
to very small angles for the higher frequencies. It would appear, therefore, that the dis-
tortion of the vertical directive pattern caused by a soil of finite resistivity might constitute
a definite limitation in working with
50°
40
30
20
10
60° 70° 80° 90° 80° 70° 60° 50°
40°
30°
20°
10°
1.2 0.8 0.4 0 0.4 0.8 1.2 1.6
50° 60°70080:)90CS00700 60° 50° 40°
very high-frequency stations. It is
seen from Fig. 16 that horizontal an-
tennas are inherently high-angle de-
vices and that vertical antennas may
also be high-angle devices except when
located over a low-loss earth.
Advantages ranging up to 10 db
(see reference 9) have been obtained
by locating short-wave antennas and
arrays at the tops of sharp declivities
or long slopes. These gams are com-
parable with those of the arrays them-
selves and are such as may warrant
considerable time in the selection of
the site of a short-wave radio station.
They may be explained either as due
to the antenna being in a position
where the field distribution is more
favorable or by saying that the de-
clivity has effectively lowered the angle
of elevation of the antenna itself.
As the factors that effect vertical di-
rectivity vary markedly from point to
point over the country it is difficult
to present any considerable number
of representative data in the space here available. However, both terrain and soil condi-
tions are important insLantenna design and should be considered when any large expen-
ditures are to be made.
30°
2.0
~0.4 0 0.4 0.8
Received Current
2.0
FIG. 16. Vertical Directional Diagrams of Horizontal
and Vertical Half-wave Antennas as Influenced by Finite
Conductivity of Earth
6-76
PASSIVE CIRCUIT ELEMENTS
30. DIRECTIVITY OF QUASI-OPTICAL ANTENNAS AND HORNS
(See reference 4)
THE
which a
HUYGENS SOURCE. The optical concept of wave propagation according to
wave front is considered an array of secondary sources is of great importance in
analyzing the behavior of quasi-
optical antennas. A formulation
consistent with fundamental elec-
tromagnetics has been given by
S. A. Schelkunoff (reference 1, 9.1
and 9.24). Commonly its usefulness
arises in situations like that, for ex-
ample, at the mouth of an electro-
magnetic horn, where we have rea-
son to believe that the currents
represented by the wave front pre-
dominate in ultimate effect over
currents elsewhere, such as those on
the outside of the horn. If we know
the distribution of intensities ovei
this aperture, Huygens' principle
can be applied. In general, over
this surface, polarization is distri-
buted in both the x and y direc-
tions, but for simplicity we write
the equation for only the first of
these. Assuming the dimensions of
the aperture great enough to give
sharp directivity, we are mainly
concerned with directions not far
removed from the center of the
main beam, which is near the axis
of the reflector. Under these con-
ditions the field at a distance r in
front of the mirror- is parallel to EQ
in the aperture and is given by the
expression:
EX. SHOWN
AT 7 CM. A 35 db
ANTENNA IS OBTAINED
USING A 64" PARABOLOID.
BEAM WIDTH IS I.6*TOTAL w
WIDTH AT I db DOWN.
PIG. 17. Nomogram — Paraboloid Antenna Data
dS being the element of area of the
aperture, and X the wavelength.
THE APERTURE. The theo-
retical performance of a non-dissi-
pative antenna, which as a trans-
mitter has a uniformly equal distri-
bution of EQ over its aperture, is
useful for comparison with actual
transmitting or receiving antennas.
It can be shown from the above
equation (see reference 10) that for
reception its effective area equals the actual area of its aperture. In other words, it can be
expected to capture from the wave all the energy "intercepted." Note, however, that an-
tennas in reception usually cannot do this, since as a rule they do not, in transmitting, pro-
duce a constant J?o over the whole aperture, and since, moreover, they may not be large
enough compared with a wavelength to validate our assumptions. As applied to trans-
mitting, the term effective area may be interpreted as the area of uniform excitation
which would give the same field at the same distance and with the same total power as
would the actual antenna.
In practice the effective area of large apertures is usually considerably less than the
actual area, and the ratio is an "efficiency" factor which usually lies within the range 0.4
to 0.7, the deficiency being due primarily to the non-uniformity of intensity across the
DIRECTIVITY OF QUASI-OPTICAL ANTENNAS, HORNS 6-77
aperture. It should be observed that requirements other than gain may make it necessary
to avoid uniformity across the aperture, such as the desirability of suppressing minor
lobes of the directional pattern.
Other points in connection with the aperture are: (1) whether or not the amplitude i«
uniform, it is usually important that both phase and polarization be the same at all points
in a plane perpendicular to the desired direction of transmission; (2) the width of the
FIG. 18. Examples of Cylindrical and Spherical Optics
aperture a of a broadside antenna is inversely as the angular beam width required in the
plane containing that dimension. At the half-power points the beam width is 51 A/a in
degrees for uniform illumination through a rectangular aperture and for non-uniform
illumination of circular or elliptical apertures it is typically 65 A/a. The gain and beam
width of circular apertures having tapers of illumination commonly used at present are
given in the nomogram, Fig. 17. When the beam width required is different in the two
planes, the aperture widths are affected inversely, an elliptical shape being common.
(See reference 11.)
Although the operation of most microwave directional antennas is best understood in
terms of generation of a plane wave front, there are notable exceptions, such as linear
end-fire arrays and polyrods.
POINT SOURCES AND LINE SOURCES. In transmitters and receivers, the power
is conveyed to and from the fl.Titp.Trrm in transmission lines which are smaller than a
Reflector
FIG. 19. Cylindrical Collimation
wavelength in cross-section, whereas in the antenna the dimensions may be of many
wavelengths. The antenna must, therefore, include a distribution system. This may
consist of a branching system, such as that used commonly in arrays. In most microwave
antennas it consists of a "primary feed" or radiator which launches a wave, this wave then
being allowed to spread in azimuth and elevation simultaneously (spherical optics), or
in azimuth and in elevation successively (cylindrical optics). The latter two processes
are indicated in Fig. 18.
In spherical expansion the wave must first be launched by a primary feed antenna which
is basically a point source. Examples will be given later. When, on the other hand,
successive cylindrical expansion is used, the wave from a point source is usually first con-
6-78
PASSIVE CIRCUIT ELEMENTS
fined between, closely spaced plates and allowed to expand in a plane, and then the line
of the wave front is converted from a circular arc to a segment of straight line; thereafter,
the three-dimensional wave front expands from this line as a cylinder whose elements are
parallel to it. These operations may be followed in the example given in Fig. 18 or
196. The line source can be formed in other ways, such as a linear array of half -wave
antennas, thus avoiding the first step of cylindrical expansion (Fig. 19o).
COLLIMATING DEVICES: REFLECTORS AND LENSES. Starting with the energy
diverging from a point source, some device is needed to convert the wave front to a plane,
that is, to make the emergent "rays" parallel. For this purpose reflectors or lenses are used.
(a) Parabolic Reflectors. The choice between a paraboloid and parabolic cylinders
(see Fig. 18), depends on many mechanical and electrical considerations. In the past,
the paraboloid has been the more used. Among the advantages sometimes claimed for it
are greater electrical simplicity, lower weight and better efficiency, better directional
pattern in the desired polarization, and adaptability to conical lobing or spiral scanning.
Rear Feed
Feed
(a)
(6)
FIG. 20. Spherical Collimation
The cylinders, on the other hand, may be simpler mechanically and possess separate con-
trol of directivity in azimuth and elevation, a point of controlling importance in some
applications.
For both types of parabolic reflectors, the feed is located at or near the focus, and the
section used may be symmetrical about the axis or off to one side (usually the former).
(b) Lenses. Dielectric lenses can be used, and they have found considerable applica-
tion in the first step of cylindrical expansion described above, i.e., in the formation of
line sources, low-loss polymers being commonly used as dielectric. For spherical optics,
however, such a lens becomes too massive. W. E. Kock (see reference 12) has developed
other types of lenses particularly suitable for microwave use, for example that which
•employs metal plates instead of dielectric material. All lenses depend on having a mate-
rial in which the phase velocity is different from that of surrounding space. If a plane
•wave were incident on a bottomless metallic honeycomb in a direction parallel to the cells,
it would pass through more or less unimpeded if the frequency were above the critical
frequency of the individual cells considered as wave guides. However, the phase velocity
in these wave-guide cells would be greater than that of light, and the material as a whole
would therefore possess a refractive index less than unity. Lenses can, therefore, be con-
structed by grading the depth of the cells in a manner analogous to that of optical lens
practice, with this difference, that a form which causes divergence in a lens of glass will
produce convergence in a lens of this cellular material; for example, a planoconcave
DIRECTIVITY OF QUASI-OPTICAL ANTENNAS, HORNS 6-79
cellular lens can be used as a collimator. If the wave is linearly polarized the cell spaces
may be made indefinitely wide in the direction of the electric vector, the lens then becom-
ing an assembly of spaced metallic plates; if in this case, however, the electric vector is
made perpendicular to the plates, the wave passes through but with substantially the
velocity of light, so that the device does not act as a lens. The lens can be given a stepwise
reduction in thickness by means of "zoning," the "riser" of the step being that length of
wave guide necessary to include one cycle less than a corresponding distance in free space.
(See Fig. 20.)
HORNS. Just as the hollow wave guide is the analog of the speaking tube, so the
electromagnetic horn is the analog of the acoustical horn in function as well as in appear-
ance. It is usually the tapered extension of a metallic wave guide, as shown in Fig. 2a
and b though it can be excited in other ways.
As in parabolic reflectors, the directional properties and gain of horns are determined
by the excitation across the aperture, and the considerations given at the beginning of
14
16
18
20 22 24
Absolute gain in decibels
FIG. 21. Optimum Horn Data. The electric vector is parallel to the dimension
this article on "The Aperture" apply approximately. The distribution of intensity in
the aperture of horns tends to be uniform in the E plane and sinusoidal in the H, a condi-
tion resulting from the maintenance of the distribution natural to a small wave guide in
passing from the throat through the taper to the aperture. Roughly then the half-power
beam width in the E plane of large horns approximates 51 X/aj?, and in the H plane
65 \/an, provided that a, the aperture dimension, is larger than one wavelength.
The phase at the center of the aperture of a pyramidal horn tends to lead that at the
edge owing to the difference in distance to the throat. For a given size of aperture this
phase difference approaches zero as the length is increased, and the best length is infinity
since any phase difference tends to reduce the gain. In a simple horn, therefore, the length
is more likely to set a practical limit than the aperture, and for a given practical length it is
often important to know the flare or aperture that will give greatest gain. This "optimum
horn" can also be defined as the minimum length of horn that will give a required power
gain. It does not provide greatest efficiency of aperture area but deliberately tolerates
an increase in area for a decrease in length.
Figure 21 gives the essential dimensions of optimum horns, conical and pyramidal,
which are taken from the article by A. P. King. (See reference 13.) The area efficiency
of a large conical optimum horn is about 55 per cent; that of a very long horn of the same
aperture is near 80 per cent. (See reference 13.)
6-80
PASSIVE CIRCUIT ELEMENTS
Among the forms of horn are the conical, biconical, sectoral, and pyramidal. Horns
can be used with lenses to avoid the undesirable phase difference across the aperture.
Solid or metal plate lenses may be used. The advantage of a lens is that it very greatly
reduces the length of the horn for a given aperture. (See Fig. 20.)
31. PRACTICAL ANTENNA SYSTEMS
In modern radio practice the highest frequencies are more than one million times as
great as the lowest, extending as they do beyond the range from 30,000 cycles to 30,000
megacycles. We have emphasized the unity of principle within this gamut of frequency.
On the other hand, in covering the field of practical antennas it is necessary to examine
types in great diversity. Space prevents any attempt to be comprehensive. In this article
we can consider only representative antennas which illustrate different engineering prob-
lems to be met in practice.
ANTENNAS FOR LOW FREQUENCIES. In Fig, le and/ are shown prototypes of
antennas important during the first two decades of "wireless," antennas which still are of
practical importance below 1000 kc. Their common characteristic is the use of a flat-top
Total Resistance, 0.4 OJuns Capacity, 0.053 Mf.
Radiation Resistance, CK05 Ohms at 18^2 KG.
FIG. 22. Typical Multiple-tuned Antenna
and a down-lead, but these have taken on many special forms — L, T, umbrella — with
single or multiple down-leads. Except in favored situations (e.g., on board a ship), it has
been necessary to build more or less elaborate ground systems comprising buried wires or
an overhead "counterpoise" in order to raise the radiation efficiency to an acceptable value,
and even then this efficiency might at the lowest frequencies be only a few per cent. Two
general methods of improving efficiency are, first, to increase the height of the towers
used (increase radiation resistance), and second, to use ground systems as already stated,
frequently accompanied by multiple tuning (decrease the ground losses) . Figure 22 shows
an Alexanderson multiple-tuned antenna having six multipled down-leads and six tuning
coils; its effectiveness depends on the fact that, although the ground resistances associated
with the various down-leads act as though in parallel to give a low resultant ground resist-
ance, radiation resistance is not correspondingly reduced. Obviously structures built on
so large a scale are very expensive and have to be designed with great attention to economic
factors. (See reference 14.)
Figure 23 shows an antenna installation for a 1,50-kc land station such as has been used
in communication with ships at sea.
Wire Rope
Operati'ng Frequency si 50 Kc.
Radiation Resistance el. 6 CO
FIG. 23. Flat-top Antenna for Operation on 150 Kilocycles
A wave antenna usually consists of a long transmission line made up of two wires spaced
about 30 in. and supported on poles about 25 ft high in accordance with standard pole
line construction. The length is often about equal to that of one wave. Although such
an antenna is a relatively poor radiator, its directional properties, together with the
rather wide band of frequencies which it can accommodate, make it exceedingly useful
in long-wave work. In particular, when used as a receiver, it is able to discriminate
markedly against static arriving from other than the preferred direction of reception.
PRACTICAL ANTENNA SYSTEMS
6-81
This provides a favorable ratio of signal to static. Because of its broad frequency char-
acteristic it is possible to attach two or more receivers and simultaneously receive several
frequencies. These signals must, of course, be arriving from the same general direction.
The directional characteristic depends among other things on soil resistivity. Such
antennas have not proved particularly effective in regions of high rainfall and high con-
ductivity. Several wave antennas may be placed in broadside array as described above
or they may be placed one back of another and sidestepped to form a staggered array.
Figure 24 shows in schematic form a wave antenna and its associated terminating net-
work. The impedance Z is equal approximately to the characteristic impedance of the
Direction of
FIG. 24. Schematic of "Wave Antenna. (The length may be as much as a mile, the height about 25
feet.)
antenna. This prevents reflection and renders the device essentially unidirectional. The
reflection transformer shown is an ingenious means whereby the accumulated signal re-
ceived between the two wires and ground may be transmitted back to a receiver located
at the incident end, over the metallic circuit consisting of the two wires themselves. (See
reference 15.)
ANTENNAS FOR MEDIUM-FREQUENCY BROADCASTING. Resonant antennas
of the general type discussed in the previous sections (e.g., Fig. 23) have been used hi
broadcasting. A more common form, however, uses a tower or mast itself as the current-
carrying conductor and radiator. Some of the forms which it takes, shown in Fig. 25,
illustrate its basic simplicity. The self-supporting towers may be of constant cross-section
or tapered to a point at the top. The masts, supported by guys sectionalized by insulators
to prevent them from taking part as radiators, are commonly tapered over the lower
fraction of their height to a single compression insulator and ball-and-socket joint at the
base. The upper portion of the mast may be tapered toward the top, but a top without
this taper is probably more common. (See reference 16.)
(«)
(c)
FIG. 25. Typical Forms of Broadcast Antenna
All the antennas shown in Fig. 25 are insulated at the base. There is a form called the
"shunt-fed antenna" (see reference 16), however, in which the tower is connected directly
to the ground network. The feed wire is connected, not at the base, but sufficiently far
above it to include an appreciable tower inductance.
For daytime coverage in this frequency range the desideratum is a strong field in the
horizontal direction, since waves leaving in an upward direction are ineffective either for
good or for ill because they are absorbed by he ionosphere. Assuming antenna resistance
to be confined to radiation and current to be distributed sinusoidally, the maximum hori-
zontal field theoretically is obtainable when the height of the radiator is 5/s wavelengths
6-82
PASSIVE CIRCUIT ELEMENTS
(225 electrical degrees, assuming that length of wave on the tower is the same as in free
space). As shown in Fig. 11, however, such an antenna will have a strong minor lobe at
30° from the vertical, and at night when ionospheric absorption tends to disappear waves
may thus be received strong enough to be comparable with the ground wave. Undesirable
fading may then be as serious as insufficient field strength would be, particularly in the
upper half of the daytime frequency range. It has, therefore, become the practice to use
radiators of that height and current distribution which gives the best compromise between
field strength and freedom from fading, and tower heights from 0.53 to 0.55 X (190° to 200°)
are widely used. (See reference 6.)
The considerations of directional pattern just described aim to protect the station's
listeners from its own sky wave. At points beyond the normal ground-wave range are
receiving sets tuned to other broadcasters operating on the same frequency, and they
must be protected from interference. New minima of signal strength in the elevation
plane must therefore be provided in that azimuth, and in view of the great distances of
the receivers the minima must be aimed far from the vertical, typically in the order of 75°.
For this purpose arrays of antennas are common ; such arrays for broadcasting have been
discussed above under "Directivity of Linear Conductor Antennas: Arrays." The proper
design of such an array is a matter of some complication; not only is the accurate locating
of towers and the specifying of their relative currents an exacting matter for calculation
but also the experimental realization of the desired amplitudes and phases in the presence
of the large mutual impedances which exist between towers makes it necessary to provide
means for accurately adjusting measuring and maintaining the currents both in amplitude
and in phase. (See reference 7.)
SPECIAL ANTENNAS FOR BROADCAST RECEPTION. Many broadcast receivers
are supplied with built-in antennas which, although inefficient as compared with the
"custom-built" antennas that are feasible in point-to-point work, give adequate perform-
ance, thanks to the high gains of receivers and the surplus signal laid down most of the
time by powerful transmitters. In the few cases where both received field and atmos-
pherics are below set noise advantage may be taken of large antennas. If the antenna is
located where the ratio of ambient noise to ambient signal is too great, it can frequently
be relocated in a quieter spot remote from the receiver and may be connected to the re-
ceiver by a shielded transmission line. This is sometimes done in apartment houses, a
broad-band amplifier then being employed to permit distribution to a large number of
users. In the nature of the case broadcast reception of medium frequencies does not
ordinarily permit the use of much directivity. (See reference 17.)
^-Reflector Curtain
FIG. 26. Arrangement of Conductors and Impedance Matching Devices in a Sterba Array
ANTENNAS FOR HIGH FREQUENCIES (2500 TO 25,000 KG). In this band of
frequencies, almost exclusively used for long distances, the wavelength is small enough to
make directivity feasible. Formerly the majority of directional-antenna installations
employed broadside arrays of half-wave elements operative over a relatively narrow band
PRACTICAL ANTENNA SYSTEMS
6-83
of frequencies. Many of these have been replaced by some form of long wire, which gives
considerable directivity at moderate cost and is sensibly aperiodic so that it may be oper-
ated at several frequencies simultaneously. Resonant antennas still find use, however,
for example, where space considerations do not permit the more extended aperiodic types.
Figure 3 shows schematics of various forms of broadside array. Several types of curtain
arrays were described by C. S. Franklin, two of which are shown in the figure. Figure 26
shows in somewhat greater detail the Sterba array, including feed lines, impedance match-
ing devices and provisions for sleet melting. (See reference 5.) As will be noted by
tracing the connections, it is possible without interrupting service to apply a 60-cycle
power to this antenna for purposes of melting sleet, a provision found in earlier forms of
linear conductor antennas (e.g., Fig. 22).
It has already been pointed out that the directional characteristic of a long straight wire
may be used to produce antennas of marked directivity. Two forms are represented in
Fig, 27. The one at the left, called a "rhombic" antenna (E. Bruce, reference 8), presents
Counterweigh.!
FIG. 27. Alternative Forms of Folded Wire Arrays
an impedance to the terminal equipment which has a constant resistive value, making it
suitable over a wide frequency range (typically 2 to 1) provided that the accompanying
shift of directivity is appropriate to the medium of propagation; in transatlantic work it is
a fortunate circumstance that the higher frequencies used by day call for a more nearly
horizontal ray than the lower frequencies used at night, making such an antenna suitable
for a wide range of conditions. When the antenna is used for transmitting a considerable
power has to be dissipated in the terminating resistance. For details of the resonant-V
antenna shown at the right of Fig. 27, as well as several other interesting types, reference
may be made to Carter, Hansell, and Lindenblad (reference 8) . Long wires are also used
in the vertical plane for directional effects, as in the "imrerted-V antenna" shown in Fig. 28.
An interesting application of array principles to reception of transoceanic telephony is
afforded by the Musa receiving antenna, the arrays of which are constructed with rhombic
antennas as the units. (See reference 18.) Over routes such as this, radio waves of high
frequency usually travel by several paths
simultaneously and arrive at different angles
above the horizontal. These components
arrive with unrelated radio-frequency phases
and even with differences of time delay which
are significant in the audio range (of the
order of a few tenths of a millisecond).
The Musa antenna (Multiple-Unit-Steerable-
Antenna) takes advantage of the spread in
angle of arrival to separate the component
waves, which may then be used singly, or in
"diversity reception," or combined with audio delay correction, etc. Since the waves are
more reliably distinguished by differences in vertical rather than azimuthal angle of
arrival, the unit antennas are arranged along the great-circle path rather than in broad-
side array. One antenna used commercially has 16 unit rhombic antennas in an array 2
miles long. The combining of units is not done in the radio-frequency circuits, but it is
accomplished at intermediate frequency through the medium of a common beating oscil-
lator. A multiple system, of phase shifters permits the separation and simultaneous re-
ception of the different components provided that they are sufficiently different in angle
of arrival.
s//y/r/y//f^^
FIG. 28. Inverted-V Antenna
6-84
PASSIVE CIRCUIT ELEMENTS
ANTENNAS FOR VERY HIGH AND ULTRA HIGH FREQUENCIES. The exten-
sive application in point-to-point and mobile services of frequencies above 30 Me has led
to a diversity of antenna types. Figure 29 illustrates a few types useful for vertical elec-
trical polarization and suitable for mounting on a pole. Except for one insulator which is
specifically labeled, all lines shown represent conductive material, insulators being omitted
in the interest of simple representation. The lower portion of (a) is the coaxial which
feeds the upper A/2 section at the middle in a series connection (the whole feed-line current
flows into the antenna) . The portion of large diameter does not touch the outer conductor
of the feed line except at the top, an arrangement which tends to minimize waves standing
on the supporting pole. In Fig. 296 there is a metallic conection between the top of the
skirt and all adjacent parts; the feed is accomplished by bringing the inner conductor
of the feed line through a hole in the outer one at a point inside the skirt which is' protected
from the weather. Figure 29c and d indicates two J-shaped antennas in which the radiating
(a)
(6)
FIG. 29. Omnidirectional Antennas Using Vertical Polarization
section is the upper half-wave of one of the feed lines above the point where the other
ends. (See reference 19.) Figure 29e shows a horizontal cross of four ground rods at the
top of a large supporting cylinder, in the hollow end of which is mounted an inner conductor
extending above it somewhat less than a quarter wavelength, the point of connection of
the coaxial line being such as to match impedances. The section below this connection
point provides a strong mechanical support for the radiating member above. (See refer-
ence 20.)
When horizontal polarization is used in ultra-high-frequency broadcasting there are
several antenna types which may be considered. With this polarization it is easier
than with vertical to increase the gain by "stacking." Several types are indicated in
Fig. 30.
The "turnstile" antenna is shown in Fig. 30a. (See reference 21.) Essentially it has
two half-wave horizontal radiating members crossed at 90° and phased in quadrature.
It is fed by a system of transmission line*. When equal currents are used in the two
radiators, the directional diagram in the horizontal plane is a circle deformed somewhat
toward a square. The vertical separation between stacked elements is one-half wave.
The turnstile antenna has been adapted for broad-band use by employment of large con-
ductors and careful attention to detail. A cross-section of such an antenna on the Empire
State Building is shown in Fig. 306, where the cigar-shaped conductors and the adjacent
central parts are surfaces of revolution about the lines AC and BD. Separate transmission
lines are provided at F for each of the four radiators. (See references 21 and 24.)
Figure 30c is an "Alford loop," which is in the form of a horizontal square the length of
whose edge is a matter of design, but which, for descriptive purposes, may be taken as
of the order of one-third wavelength. Current is supplied as shown, the currents in the
four radiating members being equal in magnitude and alike in phase as shown by the arrows
in the diagram. In stacking a vertical spacing of one-half wave is used.
PRACTICAL ANTENNA SYSTEMS
6-85
Figure 30d shows a circular antenna (see reference 22) which also is substantially a loop
antenna. The two circular radiating conductors indicated are electrically broken at B by
a parallel-plate condenser without loss of mechanical continuity and strength, the whole
assembly being capable of support from point A. The lower circle is broken at C, from
which point the system is fed in the manner of the "folded dipole," the "electrical length"
of the circumference (taking account of the loading capacitance B} being one-half wave.
Physically the circumference is less than this. This loop is attached to a vertical pole at A
and is thus metallically grounded. The pole is inside the loop. The horizontal directional
(a)
lint of Support
(«£)
Closed End
\Tower
FIG. 30. Nondirectional Antennas Using Horizontal Polarization
pattern is elliptical, the maximum difference in field strength being somewhat less than 2
db. When these units are stacked the vertical spacing is one wavelength.
The "cloverleaf" antenna, due to P. H. Smith (reference 24) is shown in Fig. 30e. This
consists of a slender tower (e.g., square) in the form of a conventional structural-steel
lattice. Up the center is a conductor, which, together with the tower itself, forms a coaxial
transmission system. The radiating "leaves" are attached as shown, forming a composite
horizontal loop. The length of each of these conductors is about 0.4 X. In stacking, a
half-wave interval is used, and, because of the resulting phase reversal, a clockwise loop
has counterclockwise loops immediately above and below it. Within a range from 88 to
108 Me one antenna can be changed from one frequency to another by varying the vertical
spacing between loops of one standard size. The horizontal diagram is substantially
circular.
The "rocket" antenna, described by Andrew Alford and shown in Fig. 30/, is a vertical
cylinder, metallically closed at both ends (in the form shown), but having an open slot
along one element of the cylinder. It is fed as shown at the point where the cylinder is
cut away by establishing a voltage across the slot. It may be thought of as a "lossy"
wave guide supporting a transverse-electric mode, the critical frequency of which is (1)
6-86
PASSIVE CIRCUIT ELEMENTS
considerably less than that of the dominant mode of an imslotted cylinder owing to par
ticipation of the slot and of the space outside the cylinder in the propagation of the wave
and (2) somewhat less than the operating frequency. The metallic ends produce a stand-
ing-wave pattern which gives an approximation to uniform vertical distribution of radiating
current over the outside, except near the ends. The antenna is in external effect somewhat
like a vertical distribution of horizontal loops. In stacking the units are placed in close
proximity. The field varies some 3 1/2 db in different azimuths. The diameter is somewhat
less than one-half wavelength, and the driving-point impedance is tuned by folding the
edges of the slot in. The "pylon" is a self-supporting antenna employing somewhat the
same electrical principle.
A horizontal square loop employing an interesting coaxial feed system has been de
scribed (see reference 23) and is shown in Fig. 30g. The sides of the square are electrically
180 in length, and adjacent sides are fed at each corner in a pushpull manner from a
vertical coaxial lying along the axis of symmetry, as shown. The "quarter-wave" sec-
tions T between the feed points and this coaxial also provide impedance transformation
See reference 30 concerning some other antennas of interest in this frequency range
^MICROWAVE ANTENNAS. Practical microwave antennas employ many component
devices in various combinations, but we can here recognize only general forms without
elaboration. Brevity may lead to omission of types of greater future importance than
those included, but this is un-
avoidable in a field so young
and lusty.
Devices used in the method
of spherical optics are illus-
trated in Fig. 31, which de-
picts two point sources, and
in Fig. 20, which shows cor-
responding methods of colli-
mation (production of parallel
rays). Figures 31a and 206
show a rear feed in which
the energy comes through the
wave guide from the left and
is emitted from the two aper-
tures toward the left. (See
reference 26.) Where appli-
Wave guld
(a.)
FIG. 31. Typical Point Sources
leierence *o.j wnere appli-
cable, rear feeds for reflectors provide a desirable method of mechanical support without
serious interference with the electrical functioning either of itself or of the reflector.
Conditions often dictate a "front" feed. Wave-guide apertures or horns are frequently
used. One of the latter is illustrated in Fig. 316, a sectoral horn in which the electric vector
might with appropriate design be either vertical or horizontal. The horn shown could
suitably be used with a paraboloidal reflector having an elliptical or rectangular shape the
greater dimension being the left-right one (note that this horn radiates a beam which is
considerably wider horizontally than vertically if the aperture has a vertical dimension
greater than a wavelength). A wave guide whose open end faces the reflector is often
used (with or without a flare) particularly where the paraboloidal reflector subtends large
angles both in elevation and azimuth.
When the feed is located in the path of the reflected wave, as in Fig. 206, part of the
energy will re-enter it and travel back along the transmission path into the transmitter.
This may be great enough to cause trouble. One of the solutions for this difficulty is
indicated in Fig. 20a, where the portion of the reflector which might cause a wave to be
returned to the feed is omitted, and the feed, which is at the focus, is directed toward the
active reflecting surface. A similar solution in which the path from feed to reflector is
enclosed in a horn is indicated in Fig. 20c. Figure 20d shows how the spherically expanding
wave from a point source can be collimated by a metal plate lens, such as has been described
above. A lens in which zoning has been introduced to reduce lens thickness is indicated
in Fig. 20e, while / suggests the advantage of a lens in shortening a highly directional horn.
• Figure 19 illustrates some principles of design involving cylindrical optics. Figures
19a and 196 include line sources employing a linear array of dipoles and a sectoral parabola
excited m the TEQ1 (rectangular) mode respectively. (Note that, according to the accepted
convention, the designation TE10 of the most common mode in rectangular wave guides
gives place to TE& when the dimension parallel to the electric vector becomes greater
than the other dimension of the cross-section.)
In some applications, such as air-borne radar, it may be necessary to have in azimuth
a sharp concentration, and in elevation a wide spread of signal having intensity distributed
DIRECTION FINDING
6-87
according to some definite function of elevation angle. When this distribution gives
uniform response along the ground the antenna is termed a cosecant antenna.
32. DIRECTION FINDING
Almost every type of directional antenna has, at some time or other, been used for
direction finding, but there are a few types which are of especial importance due to their
widespread use. (See reference 27,) Among those used in the lower frequencies are the
loop in various forms and the Adcock antenna. Microwaves have their own distinctive
methods, such as "lobing" and "scanning." The directivity may be in the receiver or
in the transmitter, and in radar it is commonly used in both simultaneously.
The loop (see Fig. Ifc) has great simplicity to recommend it but also these objectionable
features to be avoided: it does not distinguish sense (e.g., east from west); it is sensitive
to so-called antenna effect (response to electric vector independent of direction of arrival
of the wave) ; and errors are found when the arriving waves have a downward direction.
Signals arriving in a horizontal direction induce emTs in a loop in proportion to its area
and the magnetic field of the wave. At long waves most loops are small compared with a
wavelength, and therefore they tend to pick up only small signals. This bona fide emf is
therefore subject to interference from a spurious signal derived from the electric rather
than the magnetic field (a more acceptable statement would be "from e rather than from
Break in shield -
(f)
FIG. 32. Methods of Direction Finding
). Although loops ideally possess symmetry which will suppress this component,
as a practical matter it is likely to be an important source of error. Figure 32a (see refer-
ence 28) shows an application of a method for overcoming this difficulty by the addition
of a signal from an auxiliary small vertical antenna to balance out this antenna effect, thus
obtaining sharp nulls. The same circuit has provision by switching for altering the phase
of the added signal by 90°, so that it aids one of the loop maxima and opposes the other,
thus establishing the sense (east or west) . A practical embodiment of this type of circuit
is shown in Fig. 326 (see reference 28). It illustrates the important method of using a
shielded loop to reduce the effect of local induction fields and to preserve electric sym-
metry.
6-88 PASSIVE CIRCUIT ELEMENTS
The third kind of loop error occurs when the direction of arrival is not horizontal and
there has been some rotation of the plane of polarization. It is really due to pick-up in
the horizontal wires of the loop and can be combated by essentially getting rid of them.
The Adcock antenna illustrated in Fig. 32c avoids this difficulty by eliminating the hori-
zontal members and feeding the vertical ones by a shielded transmission line. '
Figure 32d depicts the Bellini-Tosi loop method of direction finding in which the loops
are fixed. By means of shielded transmission lines (usually horizontal rather than as
shown in the figure) and a goniometer, the direction can be determined in an operating
room somewhat removed from the antenna itself, which in this case may be a large one.
Figure 32e illustrates the principle of "lobing," in which by one of several devices the
direction of beam can be alternated between the positions of the solid and the dotted lines.
When the antenna is oriented so that the signals are equal, the intersection of the lobes
indicates the direction. This is the method used in many radars.
Still another method is scanning, as indicated in Fig. 32/, where the beam, preferably
very sharp, is swept periodically through a given range. The direction of maximum re-
sponse gives the desired information.
33. MISCELLANEOUS
Antenna-testing methods are being studied by the Antenna Committee of the Institute
of Radio Engineers, 1 East 79 Street, New York 21, N. Y. The report, when issued, will
represent a much more complete document than that issued by the Committee in 1938.
See reference 29. From the same source there is now available "Standards on Antennas,
etc. Definitions of Terms," price 75 cents.
For information on transmission lines see reference 25.
For information on antennas for aircraft see reference 31.
BIBLIOGRAPHY
GENERAL
Federal Communications Commission, "Standards of Good Engineering Practice Concerning Standard
Broadcast Stations." Effective Aug. 1, 1939, revised to June 1, 1944. For sale by the Superintendent
of Documents, Washington 25, D. C.
Ladner, A. W., and C. R. Stoner, Short Wave Wireless Communications. John Wiley, New York (1933).
Mcllwain, K.t and J. G. Brainerd, High-frequency Alternating Currents. John Wiley, New York (1939).
Schelkunoff, S. A., Electromagnetic Waves. Van Nostrand, New York (1943).
Terman, F. E., Radio Frequency Engineering, Chapter XIV. McGraw-Hill, New York (1937).
1. Schelkunoff, S. A., Electromagnetic Waves, Chapter XI. Van Nostrand, New York (1943).
Theory of Antennas of Arbitrary Size and Shape, Proc. I.R.E., Vol. 29, No. 9, pp. 493-521 (Septem-
ber 1941).
2. Ballantine, Stuart, On the Radiation Resistance of a Simple Vertical Antenna at Wave Lengths
below the Fundamental, and, On the Optimum Transmitting Wave Length for a Vertical
Antenna over Perfect Earth, Proc. I.R.E., Vol. 12, No. 6, pp. 823 and 833 (December 1924).
3. Foster, Ronald M., Directive Diagrams of Antenna Arrays, B.S.T.J., Vol. V, No. 2, p. 292 (April
1926).
Southworth, G."C., Certain Factors Affecting the Gain of Directive Antennas, Proc. I.R.E., Vol.
18, No. 9, p. 1502 (September 1930).
Sterba, E. J., Theoretical and Practical Aspects of Directional Transmitting Systems, Proc. I.R.E.,
Vol. 19, No. 7, p. 1184 (July 1931).
4. Friis, H. T., and W. D. Lewis, Radar Antennas. B. S. T. J., Vol. 26, No. 2, 219-317 (April 1947).
5. Sterba, E. J., Theoretical and Practical Aspects of Directional Transmitting Systems, Proc. I.R.E.,
Vol. 19, No. 7, pp. 1194-1196 (July 1931).
On calculations of characteristics of arrays, etc., see: A. A. Pistolkors, The Radiation Resistance
of Beam Antennas, Proc. I.R.E., Vol. 17, No. 3, p. 462 (March 1929) ; K. Bechmann, On the
Calculation of Radiation Resistance of Antenna and Antenna Combinations, Proc. I.R.E., Vol.
19, No. 8, p. 1471 (August 1931); P. S. Carter, Circuit Relations in Radiating Systems and
Applications to Antenna Problems, Proc. I.R.E., Vol. 20, No. 6, p. 1004 (June 1932); and
Irving Wolff, Determination of the Radiating System Which Will Produce a Specified*Direc-
tional Characteristic, Proc. I.R.E., Vol. 25, No. 5, p. 630 (May 1937).
6. Duttera, W. S., Some Factors in the Design of Directive Broadcast Antenna Systems, R.C.A. Rev.,
VoL II, No. 1, pp. 81-93 (July 1937).
Brown, G. S., Directional Antennas, Proc. I.R.E., Vol. 25, No. 1, pp. 78-145 (January 1937).
Guy, Raymond F., The New FCC Regulations, Electronics, August 1939, p.'ll.
7. Morrison, J. F., A Simple Method for Observing Current Amplitude and Phase Relations in
Antenna Arrays, Proc. I.R.E., Vol. 25, No. 10, p. 1310 (October 1937).
Kear, F. G., Maintaining the Directivity of Antenna Arrays, Proc. I.R.E., Vol. 22, No. 7, p.' 847
(July 1934).
8. Bruce, E., Developments in Short-Wave Directive Antennas, Proc. I.R.E., Vol. 19, No. 8, p. 1406
(August 1931).
Carter, P. S., C. W. Hansell, and N. E. Lindenblad, Development of Directive Transmitting
Antennas by R.C.A. Communications, Inc., Proc. I.R.E., VoL 19, No. 10, p. 1773 (October 1931).
Bruce, E., A. C. Beck, and L. R. Lowry, Horizontal Rhombic Antennas, Proc. I.R.E., Vol. 23,
•No. 1, -p." 24 (January 1935).
{Harper, A. E., Rhombic Antenna Design. Van Nostrand, New York (1941).
BIBLIOGRAPHY 6-89
9. Potter, R. K., and H. T. Friis, Some Effects of Topography and Ground on Short-Wave Reception,
Proc. I.R.E., Vol. 20, No. 4 (April 1932).
10. Friis, H. T., and W. D. Lewis, Radar Antennas, Section 3.3, of reference 4, above.
11. Cutler, C. C., Parabolic Antenna Design for Microwaves. Proc. I.R.E., Vol. 35, No. 11, 1284
(November 1947).
12. Kock, W. E., Metal Lens Antennas, Proc. I.R.E., Vol. 34, No. 11, p. 828 (November 1946).
• Kock, W. E., Metallic Delay Lenses, B.S.T.J., Vol. 27, No. 1, 58 (January 1948).
13. Electromagnetic Horns, see: Barrow, W. L., and F. D. Lewis, The Sectoral Electromagnetic
Horn, p. 41, and W. L. Barrow and L. J. Chu, Theory of the Electromagnetic Horn, p. 51,
Proc. I.R.E., Vol. 27T No. 1 (January 1939) ; G. C. Southworth and A. P. King, Metal Horns as
Directive Receivers of Ultra-short Waves, 'Proc. I.R.E., Vol. 27, No. 2, p. 95 (February 1939);
S. A. Schelkunoff, Electromagnetic Waves, Section 9.23 (Electric Horns), p. 360, Van Nostrand,
New York (1943); A. P. King, The Radiation Characteristics of Conical Horns (to be published).
14. Alexanderson, E. F. W., Transoceanic Radio Communication, Trans. AJ.E.E., Vol. 38, 1269-1285
(1919).
Alexanderson, E. F. W., Reoch, and Taylor, The Electrical Plant of Transocean Radio Telegraphy,
Trans. AJ.E.E., Vol. 42, 707-717 (1923).
Lindenblad, N. and W. W. Brown, Main Considerations in Antenna Design, Proc. I.R.E., Vol.
14, 291 (June 1926).
15. Feldman, C. B., The Optical Behavior of the Ground for Short Radio Waves, Proc. I.R.E., Vol.
21, No. 6, p. 764 (June 1933).
Beverage, Rice, and Kellogg, The Wave Antenna — A New Type of Highly Directive Antenna,
Trans. AJ.E.E., VoL 42, 215 (1923).
16. Gihring, H. E., and G. H. Brown, General Considerations of Tower Antennas for Broadcast Use,
Proc. I.R.E., Vol. 23, No. 4, p. 311 (April 1935).
Morrison, J. F., and P. H. Smith, The Shunt-Excited Antenna, Proc. I.R.E., Vol. 25, No. 6, p. 673
(June 1937).
17. Rettenmeyer, F. X., Radio Frequency Distributing Systems, Proc. I.R.E., VoL 23, No. 11, p.
1286 (November 1935).
Wheeler, H. A., and V. E. Whitman, The Design of Doublet Antenna Systems, Proc. I.R.E., VoL
24, No. 10, p. 1257 (October 1936).
Carlson, W. L., and V. D. Landon, A New Antenna Kit Design, R.C.A. Rev., VoL II, No. 1, p. 60
(July 1937).
Landon, V. D., and J. D. Reid, A New Antenna System for Noise Reduction, Proc. I.R.E., VoL
27, No. 3, p. 188 (March 1939).
18. Friis, H. T., C. B. Feldman, and W. M. Sharpless, The Determination of the Direction of Arrival
of Short Radio Waves, Proc. I.R.E., VoL 22, No. 1, p. 47 (January 1934).
Friis, H. T., and C. B. Feldman, A Multiple Unit Steerable Antenna for Short-Wave Reception,
Proc. I.R.E., Vol. 25, No. 7, p. 841 (July 1937).
Polkinghorn, F. A., A Single Sideband Musa Receiving System for Commercial Operation on
Transatlantic Radio Telephone Circuits, B.S.T.J., Vol. 19, No. 2, p. 306 (April 1940).
19. Tinus, W. C., Ultra-high Frequency Antenna Terminations Using Concentric Lines, Electronics,
VoL 8, p. 239 (August 1935).
20. Brown, G. H., and J. Epstein, An Ultra-high-frequency Antenna of Simple Design, Communications,
Vol. 20, No. 7, p. 3 (July 1940).
21. Brown, G. H., and J. Epstein, A Pretuned Turnstile Antenna, Electronics, VoL 18, No. 6, p. 102
fcj (June 1945). (Gives bibliography.)
[Lindenblad, N. E., Television Transmitting Antenna for Empire State Building, R.C.A. Rev.,
Vol. 3, No. 4T p. 387 (April 1939).
Carter, P. S., Simple Television Antennas, R.C.A. Rev., VoL 4, No. 2, p. 168 (October 1939).
22. Scheldorf, M. W., FM Circular Antenna, Gen. Elec. Rev., Vol. 46, No. 3, p. 163 (March 1943).
23. Kandoian, A. G., Three New Antenna Tvpes and Their Applications, I.R.E., Waves and Electrons,
Vol. 1, No. 2, p. 70 W (February 1946).
24. A group of short discussions on antennas for FM broadcasting, i.e., circular, broadcast loops,
super-turnstile, and cloverleaf antennas, Communications, VoL 26, pp. 40, 58 (April 1946).
25. For information on transmission lines see Section 10 in this volume (Wire Transmission Lines);
also see W. S. Duttera, New Coaxial Conductor at WTAM, Electronics, March 1939, p. 30.
J. B. Epperson, Installation of Coaxial Transmission Lines, Part I, Electronics, July 1939, p. 30,
August 1939, p. 31 (Part II; E. J. Sterba and C. B. Feldman, Transmission Lines for Short-wave
Radio Systems, Proc. I.R.E., Vol. 20, No. 7, p. 1163 (July 1932) ; W. L. Everitt and J. F. Byrne,
Single-wire Transmission Lines for Short-Wave Antennas, Proc. I.R.E., VoL 17, No. 10, p. 1840
(October 1929).
26. Cutler, C. C., Design of Parabolic Antennas. See reference 11 above.
27. Keen, R., Wireless Direction Finding, 3d Ed. EifFe & Sons, London (1938).
28. Martin, H. B., Small Vessel Direction Finding, R.C.A. Rev., Vol. II, No. lf p. 69 (July 1937).
29. Report of the Antenna Committee entitled: "Standards on Antennas," to be published by the
Institute of Radio Engineers, 1 E 79 Street, New York 21, N. Y.
Cutler, C. C., A. P. King, and W. E. Kock, Microwave Antenna Measurements. Proc. I.R.E.t
VoL 35, No. 12, 1462 (December 1947).
30. Hidetsugu Yagi, Beam Transmission of Ultra Short Waves, Proc. I.R.E., VoL 16, No. 6, p. 715
(June 1928).
Kraus, John D., The Corner-Reflector Antenna, Proc. I.R.E., VoL 28, No. 11, p. 513 (November
1940).
31. Antennas for Aircraft: P. C. Sandretto, Principles of Aeronautical Engineering, McGraw-HilL.
New York (1942) ; F, D. Bennett, P. D. Coleman, and A. S. Meier, The Design of Broad-Band
Aircraft-Antenna Systems, Proc. I.R.E., VoL 33, No. 10, p. 671 (October 1945); Fit. Lt. C. B.
Bovill, J. AJ.E.E. (London), VoL 92, Part III, p. 105 (June 1945); G. L. Haller, Aircraft
Antennas, Proc. I.R.E., VoL 30, No. 8, p. 357 (August 1942).
SECTION 7
VACUUM-TUBE CIRCUIT ELEMENTS
AMPLIFIERS
^Tf BY Lor E. BABTON PAGE
1. Class A Amplifiers ................... 03
2. Class B Amplifiers ................... 15
3. Class C Amplifiers ............ . ...... 24
4. Regeneration and Its Prevention ....... 28
SPECIAL-PURPOSE AMPLIFIERS
BY E. L. CLAKK
5. Wide-band Amplifiers ................ 31
6. Cathode Followers ................... 47
7. Grounded-grid Amplifier .............. 49
8. In-phase Amplifiers .................. 50
9. Negative-feedback Amplifiers .......... 51
10. Pulse Amplifier ...................... 55
rNTERMEDIATE-FREQUEH'CY
AMPLIFIES
BY CnAjaLES J. Erases
11. Factors Affecting the Choice of Inter-
mediate Frequency ................. 56
12. Narrow- and Medium-bandwidth I-f
Amplifiers ......................... 58
13. Wide-band I-f Amplifiers ............. 63
MODULATORS
BY J. E. YOUNG
14. Types of Modulation ................. 71
15. Grid Modulation ..................... 73
16. Plate Modulation .................... 74
17. Comparison of Modulation Systems .... 75
DETECTORS
^xx. -^T VEHNON D. LAXDON PAGE
18. Square-law Detection 76
19. Linear Detection 79
OSCILLATORS
BY CASL C. CHAMBERS
20. Vacuum-tube Oscillators 83
21. Electromechanical Oscillators 91
22. Cavity Resonators, by I. G. Wilson and
J. P. Kinzer 95
POWER SUPPLY
BY J. E. YOUNG
23. Receiver Power Supply 106
24. Transmitter Power Supply 108
25. Rectifier Circuits 110
RADIO RECEIVERS
BY VEBNON D. LANDON
26. Types of Receivers 117
27. Fidelity Characteristics 125
28. Random Noise 127
RADIO TRANSMITTERS
BY J. E. YOUNG
29. Intermediate-radio-frequency Amplifiers 129
30. Power Amplifiers 131
31. Audio Amplifiers 134
32. Telegraph Transmitters 134
33. Installation of Radio Transmitters 134
7-01
VACUUM-TUBE CIRCUIT ELEMENTS
AMPLIFIERS
By Loy E. Barton
An amplifier is a device for increasing the energy associated with any phenomenon
without appreciably altering its quality.
Amplifiers used in communication circuits almost invariably employ thermionic vac-
uum tubes as the amplifying elements. The vacuum tube is practically a pure resist-
ance device at low frequencies. As the frequency increases to a point where the inter-
electrode capacity impedance becomes appreciable with respect to the internal resistance
of the tube a phase shift is introduced which alters gain or amplification.
At still higher frequencies the time required for the electrons to reach the plate is ap-
preciable with respect to a quarter cycle. When this transit time is about 20 to 30
electrical degrees the amplifier characteristics are modified considerably. These ampli-
fiers still fall in one of the three basic classes of amplifiers.
A class A amplifier is an amplifier in which the grid bias voltage permits a steady plate
current flow of such a value that the plate current varies directly as the grid voltage for
the complete cycle of 360 electrical degrees. The resulting output voltage for an ideal
class A amplifier is an exact reproduction of the grid voltage.
The characteristics of the class A amplifier are low power output with a theoretical
maximum plate power efficiency of 50 per cent and an operating efficiency of about 30
per cent or less at full power outputs. The plate dissipation is maximum at zero out-
put, and the plate circuit output network may be tuned or untuned for an undistorted
output. The average value of plate current does not change during the cycle so that
the input plate power is constant.
A class B amplifier is an amplifier in which the grid voltage permits essentially zero
plate current with no signal applied to the grid and the plate current is proportional to
the grid swing when the grid swings in a positive direction from the bias point so that
plate current flows for approximately 180 electrical degrees.
The characteristics of the class B amplifier are comparatively high power output with
a theoretical maximum plate efficiency of 78.5 per cent; in practice the efficiency ap-
proaches 65 per cent at full output. The plate dissipation is a minimum and is com-
paratively low at zero signal, increasing rapidly to approximately constant value at about
25 per cent full output. However, the power input to the plate increases, with signal
and power output, until the peak output is reached. Therefore, the plate current is a
variable and the plate supply voltage should have good regulation. The class B am-
plifier may be used as a single-tube tuned-plate circuit amplifier or the plate circuit may
be untuned provided two tubes are used in a pushpull manner with appropriate input
and output transformers.
A class BI amplifier is an amplifier biased and operated as a normal class B amplifier
except that the grid swing does not go into the positive region.
In general such an amplifier uses low-mu tubes in order that high plate currents may
be reached without driving the grid into the grid-current region. The efficiency of this
amplifier is lower than that of an amplifier in which the grid is driven to plate-current
saturation, and the power output is lower. However, the grids take no power so that
input circuit losses and distortion may be low.
A class ABi amplifier is an amplifier so biased that the pushpull ^tubes act as a class A
amplifier for low grid swings and go into class BI operation at higher grid swings. The
grids are not driven positive.
The only advantage of this type of operation is that somewhat higher outputs may be
obtained for a given plate dissipation than can be obtained for class A operation and a
cathode resistor can be used for self-bias. However, distortion is comparatively high.
A class- AB2 amplifier is similar to the class ABi amplifier except that the grids are
driven into the positive region for higher outputs.
The characteristics of the class AB2 amplifier are much the same as those of the class
ABi except that the power output is higher, and the grid driving problem is about equal
to that of the class B amplifier.
7-02
CLASS A AMPLIFIERS 7-03
A class C amplifier is an amplifier in which the grid bias voltage is appreciably higher
than the bias required for plate-current cutoff, and the plate current flows for a period
less than 180 electrical degrees during the half cycle when the grid swing is positive with
respect to the bias voltage. The grid swing is usually to the point of plate-current satu-
ration, in which case the rms plate current is proportional to plate voltage and is not
proportional to the grid voltage.
The characteristics of the class C amplifier are high power output and an average plate
efficiency in practice of 70 to 75 per cent, which may reach 85 to 90 per cent under special*
conditions. (See Fig. 35, p. 7-27, and discussion.) The theoretical maximum effi-
ciency for the class C amplifier is 100 per cent.
1. CLASS A AMPLIFIERS
GENERAL USE. The class A amplifier is used for audio-frequency and radio-
frequency voltage amplification, principally because the output voltage is a direct func-
tion of the input voltage. The amplifying action of the vacuum tube follows from the
equations developed for its plate current in Section 5. If all the terms but the first in
eq. (17), p. 5-43, are negligible, the voltage drop due to the plate current of the vacuum
tube flowing through an external impedance is
or for a particular component of periodicity &m
E, = -2^=- (la)
Tp + Zm
This voltage is a magnified replica of the grid voltage and is said to be amplified.
The voltage amplification is the ratio of the change in voltage across the external load
to the change in input voltage, or
V.A. = / *•». = = (2)
V(r + rp)2 + xm* *»
if there is no drop in the external grid circuit. Two special cases are of interest: First,
when the load is a pure resistance; V.A. = pr/(rp -j- r} which will equal 0.9 jtt when
T — 9rp. Second, when the load is a pure reactance, V.A. ~ tucm/ V rp2 -{- xm*, which
will approximate 0.9 JJL when xm = 2rp.
The power amplification is the ratio of the power delivered by the output circuit to
the power supplied to the input circuit, or
l(rP + r)2 -f xJKn + re}
where z" is the total impedance in the grid circuit.
For small power outputs, the power amplification is very high and is usually limited
only by the input circuit losses.
Cascade Amplifiers. The limitations of voltage and power amplification obtainable
with one tube make it frequently desirable to use two or more tubes in cascade by coup-
ling the plate circuit of the first tube to the grid circuit of the next tube, etc. Each tube
with its associated circuits is called a stage of the amplifier, and the whole is termed a
multistage or cascade amplifier. Cascade amplifiers are usually classified by the method
of coupling used.
The amplification per stage is defined as the ratio of the grid voltage of one tube to the
grid voltage of the preceding tube. This is frequently expressed in decibels.
For the resistance-coupled amplifier shown in Fig. 1, it is
V.A. •. -- - - (4)
rpTj* rp TyXjz
— ; — { --- r 1 — 3 - r~
2t22 T Zi?
For low frequencies, and when the grid biasing voltage is always negative, the amplifi-
cation limit per stage of this type of amplifier is ft.
^-
7-04
VACUUM-TUBE CIRCUIT ELEMENTS
A direct resistance coupled amplifier of the type shown in Fig. 1 is used when it is
necessary that a d-c voltage be amplified. It will be noted that the required B voltage
increases with each stage and that independent filament supplies are needed for direct-
heated tubes. In the case of indirectly heated cathodes a separate heater supply is usu-
ally needed because of the excessive heater cathode potential.
FIG. 1. Direct" Resistance Coupled Amplifier, Common B and C Batteries, Separate A Batteries
The amplification per stage of the resistance-capacitance coupled amplifier shown in
Fig. 2 is
V.A.
zc + rp rpzc rpZc ,rP
I --- 1 -- ~t --- 1 --- r J-
(6)
in which zc is the reactance of the coupling condenser C. A reactance may be substituted
for either r or TK, or both, in which case these constants are changed from r to z in eq. (6) .
PIG. 2. Resistance-capacitance Coupling
If the input impedance to the second tube is very high and the impedance of the coupling
condenser negligible eq. (6) reduces to
VA. = £— - (6a)
from which it is seen that the higher the resistance of the parallel combination of r and
TK. the greater the realized amplification will be. The limiting value of TK. is usually
1 megohm or less, so that it is of little value to make r greater than 75,000 to 100,000 ohms.
The plate voltage supply must be great enough to operate the tube at a desirable point
and to supply the drop in the load resistor in order to obtain maximum voltage in the
succeeding tube. A lower plate supply voltage may be used with a corresponding re-
duction of bias if maximum voltage output is not required. This will have little effect
on the amount of amplification obtained.
Cascade operation of two or more resistance-capacitance coupled audio amplifier stages
is subject to a low-frequency oscillation or "motor-boating," resulting from a feedback
of low frequencies due to the common a-c impedance of the plate supply at frequencies
so low that the filter condensers are not effective. To correct the motor-boating diffi-
CLASS A AMPLIFIERS
7-05
culty, it is usually necessary to limit the low-frequency response or isolate one or more
of the resistance coupled stages. The low-frequency response is most easily reduced by
decreasing the size of the coupling condenser (C in Fig. 2).
A transformer-coupled amplifier is shown in Fig. 3 and its equivalent circuit in Fig. 4.
In the equivalent circuit, account is taken of the distributed capacitances (Cj and Cg)
FIG. 3. Transformer Coupled Amplifier
FIG. 4. Equivalent Circuit of the Transformer Coupled Amplifier of Fig. 3
of the windings and of the distributed capacitance (CM) between windings. The trans-
former windings are assumed to be poled so that the effect of this latter is a minimum.
The voltage amplification of each stage is then
V.A. =
where
__
, zs
— J-
Zx =
23 H- 24 — j2t»M —
- 3
and
Z3 w^
Note that if the incidental resistances of the transformer windings are neglected ZM*
Zx, and zy are all pure imaginaries.
The maximum value of V.A. with respect to 0-5 occurs under two conditions: one value
(infinity) will give maximum value of V.A. for all frequencies; the other value, dependent
in a complicated manner on the mesh parameters, will give a maximum for only one
particular frequency. The same result is found when x^ is considered the variable.
These correspond to the cases of tuned and untuned transformers. (See p. 6-08.)
7-06
VACUUM-TUBE CIRCUIT ELEMENTS
When substantially equal amplification is required over a broad frequency range the
distributed capacitance should be made as small as possible. Assuming xz and #5 infi-
nite and CM zero, eq. (7) reduces to
24) + u*M*
By tuning primary and secondary circuits as shown in Fig. 5, the maximum amplifi-
cation (at one frequency only) is
VA. =
7-4)
(76)
A
D
^ff
^!La
A
D )
<
<
? s
C2
ilililil
Out
<
I|I|I|I|
i
^
-if
illhiilll
FIG. 5. Tuned Transformer Coupled Amplifier
Output
FIG. 6. Tuned Coupling. The tuned circuit is La-Lb-C. The coil Zk and the capacitor Ck are
inserted to get proper bias on the grid tube 2.
A1
' *~d
5 ^rc» j?f >
0
Outf
i
Tl
-ill!
_^
-S
-1
r~
lidhlil—
FIG. 7. Tuned Coupling. The tuned circuit is Ca-Ct>-L. The coil Zk is inserted to get proper
potential on the plate of the first tube.
Other forms of tuned amplifiers are shown in Figs. 6 and 7. For the resonant fre-
quency the amplification of the circuit of Fig. 7 is
VA. =
where z
fi - *r
\Z 2i2
(8)
CLASS A AMPLIFIEES
7-07
Performance. Certain tube characteristics are supplied by the tube manufacturers
(see Section 4) which are used to predict the performance of tubes as class A amplifiers;
representative curves and tube constants will be given herein with sample calculations of
performance. A typical general-purpose triode is the 56-type tube whose plate char-
acteristics are given in Fig. 8.
It will be noted that each
curve of plate current against
plate voltage is drawn for a
given grid or bias voltage
denoted as Ec. From these
curves, the various constants
of the tube may be calculated
as explained in the section
on vacuum tubes. The con-
stants for the 56, as calculated
from Fig. 8, at approximately
238ftvolts at the plate, 13.5
volts bias, and 5 ma plate cur-
rent, are plate resistance (rp)
equals 10,000 ohms, amplifica-
tion factor (AI) equals 15, and
the grid plate transconductance
equals 1500 micromhos.
200 300
Plate Vjolts
400
500
FIG. 8. Type 56, Plate Characteristics
INPUT CIRCUIT CALCULATIONS. A typical circuit for the 56 tube as a trans-
former-coupled audio amplifier is shown in Fig. 9 and its approximate equivalent in
Fig. 10. If the tube used in Fig. 9 is the 56 type with characteristics as shown in Fig. 8,
and its various constants are as indicated above, the constants of the circuit and per-
formance of the tube may be calculated as follows:
The self bias resistor, rlt is calculated for a 13.5-volt operating grid bias voltage with
5 ma plate current, in which case, according to the curves in Fig. 8, the voltage across
the terminals marked minus and plus for plate supply should be 250 volts and the actual
plate voltage will be about 236.5. The value of the resistor, ri, is 13.5/0.005 = 2700 ohms.
The by-pass condenser, Ci, must effectively by-pass n at the lowest audio frequency
desired so that the pulsating plate current through TI will not generate an audio voltage
appreciable compared to that applied to the grid. The voltage across rx is out of phase
with the input voltage so that the low-frequency gain may be lower than the gain at other
Type 56
FIG. 9. Transformer-coupled Class A Amplifier
FIG. 10. Equivalent Cir-
cuit for Fig. 9
frequencies if the impedance of C\ is large. The capacitance, Cz, across the plate sup-
ply may be the plate-supply filter condenser but, in any case, must have sufficiently low
impedance at the lowest desired frequency to by-pass the plate supply effectively unless
the a-c impedance of the plate supply is very low.
OUTPUT CALCULATIONS. The dotted resistance r in Fig. 9 is the equivalent im-
pedance (as nearly unity power factor as possible) of the primary of the transformer,
T, with the load resistance, r&, transferred from the secondary into the primary. It will
be noted that r is in series with the plate of the tube and may be represented by a load
line drawn through the operating point at 5 ma plate current and 13.5 volts bias in
Fig. 8.
The proper value for this resistance is obtained by drawing a line through the operating
point and the point on the zero grid voltage curve representing the maximum desired
value of the operating plate current (in this case 9 ma, since experience has shown that
an 80 per cent change in plate current is a reasonable value to assume). A check along
the load line as drawn indicates that, if the grid swings in a negative direction to double
the grid voltage of 13.5 volts, the decrease in plate current is only 3.2 ma, approximately.
7-08
VACUUM-TUBE CIRCUIT ELEMENTS
This load line represents approximately 43,000 ohms and is r as shown in Fig. 9. The
approximate second harmonic under 4hese conditions may be calculated by the following
formula:
H~ -^6 min —
-
, , , . 1 ,
per cent second harmonic approximately
•
- - - - — = pr c xi
2(/ b max — i~b min) ~ .- , r ^n > • i , > (Q\
= 5.5 per cent for 80 per cent increase in plate current f W
as assumed above J
in which I& is the "no-signal plate current," J& max is the peak plate current, and 7$ min is
the minimum plate current.
Note that if the maximum current change is equal on each side of the operating value
the second harmonic is zero, since (I& max — I&) — (1 & — /& min) = 0. If intermediate
points are considered and it is found that equal grid-voltage increments do not cause
equal plate-current increments throughout the range, higher harmonics will be present.
(See p. 5-47.)
The average power output may be calculated by the following formula, which is readily
derived from peak values of a-c voltages and currents.
(•* 6 max — •*& min) (Eb max ~" Eb min)
8
power output or 0.28 watt approximately, I
for full grid swing in the above case J
in which Eb max is the maximum plate voltage and Eb min is the minimum plate voltage.
The theoretical maximum /& max for the class A amplifier is 2I&, and the minimum J&
is zero. The corresponding theoretical maximum Eb max is 2Eb, and the minimum
is zero.
The plate power input is expressed by the formula Eblb = watts input. Therefore,
the plate efficiency at maximum output is
PL eff. =
The load resistance is
b max — ?b min) (Eb max ~ Eb min)
8EbIb
= 23 per cent
Bin)
(Ib max — •* b min)
43,000 ohms approximately
(ID
(12)
The total plate voltage swing is approximately 314 volts, and the total grid swing is
27 volts, which is
,-, max ^ mn. = —=• — 11.6 approximate actual amplification by the tube (13)
\&c max — &c min) ^'
In the above circuit the transformer T may be designed as a voltage coupling trans-
former to supply a secondary load as high as 200,000 ohms or more, an output impedance
which is not particularly difficult to obtain especially if a choke voltage feed is used as
shown in Fig. 11, so that the d-c plate current does not go through the transformer pri-
FIG. 11. Shunt Transformer-coupled Amplifier
mary. The turn ratio would be the square root of the impedance ratio or a turn ratio
of the primary to secondary of at least 2.2. The total amplification of this amplifier
stage including the transformer is 11.6 X 2.2 = 25.5, approximately.
The above condition is also approximately the condition for maximum power output.
If the calculated distortion is too high, the grid swing may be reduced with a correspond-
ing reduction of power output. In actual practice, the grid swing is usually very small
if the amplifier is used as a voltage amplifier so that maximum voltage output is not ob-
tained but the voltage amplification is the same; in such a case the second harmonic may
be negligible (far less than 1/2 per cent) .
CLASS A AMPLIFIERS 7-09
PERFORMANCE CALCULATIONS FROM TUBE CONSTANTS. Referring to the
equivalent circuit shown in Fig. 10, the voltage amplification of the combination of
Fig. 9 and Fig. 8 may be calculated from the constants of the tube by means of the fol-
lowing formulas:
V.A.
7/
+ r
— 12.2 gain without transformer (14)
in which Eg is the rms grid voltage and the other constants are as denned above.
The power output for full grid swing of 13.5 volts peak or an rms value of 9.6 volts is
P. out » - 2 - -- = 0.27 watt (15)
TP
It may be seen that, by using the constants of the tube in the equivalent circuit of
Fig. 10, the performance calculations do not differ materially from the performance cal-
culated from the curves in Fig, 8. The small discrepancy may be accounted for by the
fact that the constants of ju and rp used in eqs. (14) and (15) are obtained by using smaller
increments of voltage and current changes than are used in eqs. (10) and (13) ; in other
words, the effect of distortion is neglected.
It will be seen that, if the circuit shown in Fig, 9 is used, the only difference between a
voltage and power amplifier is the design of the transformer, T, which, in a voltage ampli-
fier works into a high resistance and in a power amplifier works into the desired load,
the turn ratio being chosen to present the same equivalent primary impedance.
If in the resistance coupled amplifier the load resistance is 43,000 ohms, the gain is
the same as calculated for the above case if TK ^> r. The same load line as shown in Fig. 8
may be used provided the plate supply voltage is equal to the value indicated by the in-
tersection of the load line and the zero plate-current axis. This plate voltage is approxi-
mately 460 volts instead of the 250-volt supply for the transformer-coupled case.
POWER OUTPUT AND PLATE EFFICIENCY. In the operation of vacuum tubes
as amplifiers (also as oscillators, or detectors) at low power levels it is usually desirable
to get as much output signal power as possible from a given tube regardless of the plate
efficiency (the ratio of the output signal power to the input plate supply power). Under
such conditions there is usually one of two parameters limiting the power output, namely,
the input signal voltage in amplifiers and detectors, or the plate supply potential in the
case of all vacuum-tube operation.
When the input signal voltage is the limiting factor, and the tube is operating over a
linear part of its characteristic (for detectors this means linear with respect to its detec-
tion characteristic — see Detectors, p. 7-76) , the vacuum tube can be considered a gener-
ator with an internal resistance. Then the maximum power output occurs when the
load is a pure resistance equal to the internal resistance.
Frequently the input voltage available is large enough so that for the given plate sup-
ply voltage the introduction of distortion is the limiting factor. Using the Taylor's
series development of the plate current up to and including the second power term, War-
ner and Loughren (Proc. I.R.E., Vol. 13, 709 [1925]) showed that under these conditions
the maximum undistorted power output is obtained when the load was resistive and
equal to twice the internal resistance. Experiment has generally shown this to be ap-
proximately correct for amplifiers using low amplification triodes in class A operation
but that no such simple rule applies in high-mu triodes, tetrodes, pentodes, and class B
operation of triodes. The optimum value of load resistance is usually determined ex-
perimentally and forms part of the operating data furnished by the tube manufacturer.
When vacuum tubes are operated at high power levels it is usually economically neces-
sary to consider the plate efficiency. This is given by the formula
Eff.
where to is the component of the current in the plate circuit having the desired output
frequencies and amplitudes; eo is the corresponding voltage drop across the load ZL, the
resistance component of which is TL; t is the instantaneous value of the plate current;
JEb is the plate supply potential; and T7 is a complete period of i.
7-10
VACUUM-TUBE CIRCUIT ELEMENTS
When the current i is given in the form
i = IQ + /i cos cat + /2 cos 2cat •+•
the plate efficiency becomes
Eff. -^
FIG. 12. Pushpull Amplifier
when the fundamental is the desired frequency of the output power.
PUSHPULL AMPLIFIER. Figure 12 represents a pushpull amplifier, which has sev-
eral advantages over the single-ended amplifier. A class A pushpull amplifier does not
take a pulsating current
from the plate supply for
the ideal condition, and in
practice the variation of
supply plate current is neg-
ligible. This essentially
constant plate current per-
mits the omission of the by-
pass condenser that is re-
quired in a single-ended
class A amplifier, shown as
Ci in Fig. 9. Another ad-
vantage of the pushpull am-
plifier is that the d-c magnetizing current in the primary of the plate transformer is
balanced out, which simplifies the plate transformer design. (See p. 6-17.)
The equivalent circuit of the pushpull class A amplifier is shown in Fig. 13, which is
similar to the circuit shown in Fig. 10, except that the resistances of both plates are in
series with the load resistance. In order that the load resistance r of 43,000 ohms be
obtained for the 56-type tube as discussed for the single-ended amplifier, it is necessary
that the primary impedance of the loaded output transformer be 86,000 ohms, which is
not very practical for voltage amplifier purposes, because of the large number of turns
required in the primary. Another disadvantage of the pushpull voltage amplifier is that
one-half of the total input voltage is available for each grid and the increased power out-
put increases the output voltage into a given resistance
by only approximately 40 per cent. Therefore, the
actual decrease in voltage gain by using two tubes in
pushpull-instead of one single-ended tube is about 20 per
cent.
The calculations of power output of the class A push-
pull amplifier may be made by using eq. (10) or (15), if
the results are multiplied by 2. The load resistance is
\
•-wwvv-
FIG. 13. Equivalent Circuit for
Class A Pushpull Amplifier
calculated by multiplying eq. (12) by 2 so that the transformer primary impedance (plate
to plate) is double the value obtained for a single-ended amplifier.
TRIODE VOLTAGE AMPLIFIER. The class A voltage amplifier in general uses a
special high-gain type of tube instead of the general-purpose tube such as the 56. The
tube characteristic desired is indicated by eqs. (13) and (14) . The higher the amplifica-
tion constant ju, other constants being equal, the higher will be the voltage amplification.
Tubes designed primarily for voltage amplifiers of the triode type are the 240, 841, 85,
203A, and others. The general-purpose tube such as the 56 discussed in some detail
also has quite extensive application as a voltage amplifier, where interstage coupling
transformers are used. In general, the plate resistance of the high-amplification-factor
tubes is quite high, so that such tubes are employed principally in resistance-coupled ampli-
fiers. Because of the general use of screen-grid tubes as high-gain amplifiers the triode is
becoming less common as a voltage amplifier except where coupling transformers are used.
TRIODE POWER AMPLIFIER. The above discussion applied primarily to the
triode as a class A amplifier in which, in general, the grid is not driven into the positive
region. With this limitation for grid excitation, it is seen from eq. (10) that the higher
the plate-current swing for a given plate-voltage swing the greater will be the power out-
put and correspondingly the greater the plate dissipation. Therefore, a power tube to
operate as a class A amplifier, without positive grid swing, should be a low-plate-resistance
tube with a correspondingly low amplification constant and capable of relatively high
plate power dissipation. The various types of triode tubes primarily designed for the-
class A power output service are the 31, 45, 2 A3, 842, 250, 845, 849, and 848. The type-
31 tube is the small battery tube rated as 0.375 watt output; the 848 is a large water-
cooled tube rated at approximately 1900 watts output as a class A amplifier.
CLASS A AMPLIFEBES
7-11
200 300 400
Plate Votts
FIG. 14. Type 2A3 Plate Characteristics
A typical low-plate-resistance tube designed as a class A power output tube is the 2A3,
the plate characteristics of which are shown in Fig. 14. Calculations similar to those
made on the 56 tube indicate that about 3.5 watts output can be obtained from the 2A3
with a load resistance of 2500 ohms, a bias of 43.5 volts, a plate voltage of 250, and a
plate dissipation of 15 watts at zero out-
put. The plate dissipation decreases from
full value at no signal to the full value
less the output power with signal. The
above 15-watt plate dissipation for the
2 A3 decreases to 11.5 watts at full output.
PENTODE VOLTAGE AMPLIFIER.
The class A pentode amplifier may be
used as a voltage amplifier for audio or
radio frequencies. The fundamental cal-
culations of power output and determina-
tion of load (r) lines is essentially as dis-
cussed for the triode amplifier, but certain
details of the calculations are different.
One of the principal differences is that
the amplification factor is much higher
than the amplification obtained in prac-
tice because the plate resistance, rp, of
the tube is much higher than it is feasible
to equal with a load resistance, r. Because of the very high amplification factor of pen-
todes as well as tetrodes with a correspondingly high plate resistance, eqs. (10), (12),
and (13) are much more useful than eq. (14). The transconductance, gm, for the pen-
todes and tetrodes is also quite useful in performance calculations.
Referring to the definition and means by which the transconductance was obtained
(as given in Section 4) , it will be noted that the condition for obtaining data for gm cal-
culations is that the resistance in series with the plate is zero or at least sufficiently low
not to alter the observed plate-current change for a given grid-voltage change. It may
be seen from the plate current characteristic of a type-57 pentode, as shown in Fig. 15,
that the slope of a load resistance line drawn through the indicated operating point does
not alter the plate-current change appreciably for a given grid voltage swing. This tube
is used extensively for radio-frequency and audio-frequency high-gain amplifiers. Ex-
cept where maximum power or voltage swing is desired, it is not necessary to use the
plate-current curves to make
performance calculations (ex-
cept to prevent overloading),
as such calculations can be
readily made from the con-
stants of the tube. For the
conditions as given in Fig. 15,
the transconductance at —3
volts bias is 1225 micromhos,
the plate resistance is given
as greater than 1.5 megohms,
and the amplification factor
is greater than 1500. It is
obvious that, with the more
or less indefinite amplification
factor and plate resistance,
the equations involving these
constants are of little value in
calculating the voltage gain
in a 57 amplifier. However,
100
200 300
Plate Volts
400
Screen VoTts » 100 Suppressor Volts » 2
FIG. 15. Type 57, Plate Characteristics
since the gm of the tube is definite within limits and the above constants are high, the
plate-current change for a given signal EK is: Eggm — I? and I^r — Ev. Therefore, the
voltage gain is
-£ = gmr = Voltage gain (16)
For the assumed conditions and a load of 100,000 ohms the voltage gain is
1225 X 10"6 X 100,000 = 122.5
7-12
VACUUM-TUBE CIRCUIT ELEMENTS
The above value of voltage amplification is approximately 6 per cent high if the plate
resistance of the tube is 1.5 megohms, but such corrections are usually unnecessary unless
great accuracy is required, and then it is advisable to measure the transconductance of
the tube, as well as the plate resistance, at the point of actual operation. A decrease of
load resistance to 50,000 ohms reduces the gain to approximately 50 per cent of the above
calculated value, and the accuracy is greater because of the lower value of load resistance
relative to the actual plate resistance.
In an audio amplifier it is possible to attenuate the high audio frequencies considerably
if the load or coupling resistance is sufficiently high so that the shunting capacitances
appreciably lower the imped-
ance of r. These capacitances
are the plate to suppressor grid
capacitance of the 57 amplifier
plus the capacitance of the tube
or device to which the amplifier
is coupled. The output capaci-
tance of a 57-type tube as an
audio amplifier is about 6.5 y.yJL ,
and the input capacitance to a
similar following stage of am-
plification is about 5 wi or a
total of about 12 /j/zf, the im-
pedance of which is about 1.3
megohms at 10,000 cycles,
which would not appreciably
affect the above 57 amplifier
with an r of 100,000 ohms, at
the higher audio frequencies.
•300
FIG. 16. Type 58, Plate Characteristics
1500
Plate
Volts «250
Screen Volts=100
Suppressor Volts=rO
As commonly used the voltage output from a 57 amplifier is so small that little non-linear
distortion is introduced.
If the tube is used as a radio-frequency amplifier, the plate impedance is obtained by a
parallel-resonant, or an equivalent, circuit in series with the plate, and for known equiva-
lent series impedance of the plate circuit the voltage gain may be calculated as indicated
above. Since the tube resistance is very high, the selectivity of the amplifier for tuned
output is essentially the selectivity of the tuned plate circuit.
VARIABLE-GAIN PENTODE VOLTAGE AMPLIFIER. The 57 tube just discussed
is not well adapted to use as a variable-gain control tube by changes in the bias. A tube
designed primarily for a bias-controlled vari-
able-gain amplifier is known as the type-58
tube, the characteristics of which are shown
in Figs. 16 and 17. Since the plate resistance
of the tube is approximately 800,000 ohms or
more, the gain as calculated by eq. (16) is quite
accurate and the gain decreases as the negative
grid-bias increases because the transconduct-
ance decreases for increased bias. The distor-
tion in the output of this tube is greater than
for the 57-type tube, and for this reason the
58-typeisnot generally used for an audio voltage
amplifier. If the plate circuit of the 58 is tuned
and the grid-voltage swing is not too great, little
distortion results from the use of this tube in
the radio-frequency system of a receiver. The
bias may be supplied from an automatic vol-
ume-control system, the output of which supplies Fm> 17 T 58> Transconductance
a bias that is proportional to the carrier
value of the received signal, or may be controlled manually, or by a combination of the
two. The type-58 or other tubes with the approximate exponential grid voltage vs. plate
current characteristics (such as types 34, 35, 39, 78, 6C6) are almost universally employed
in receivers so that a simple bias control may be used to control the sensitivity of the
radio-frequency amplifier. (See Ballantine and Snow, Proc. I.R.E., Vol. 18, No. 12,
p. 2102 [December, 1930].) Such a system permits an automatic volume control to de-
termine the output level to the audio system so that all stations above a predetermined
level and with a given percentage of modulation will be reproduced at essentially the
same volume.
21000
500
40 30 20
Control Grid Volts
CLASS A AMPLIFIERS
7-13
It will be noted that, of the tubes listed, all are pentodes except the early exponential
tube, type 35. The principal reason for the pentode construction is that the plate voltage
swing is not limited by the
screen-grid voltage for the
pentode as for the screen-grid
tube.
PENTODE POWER AM-
PLIFIER. This latter charac-
teristic of pentode tubes per-
mits comparatively large power
outputs from tubes designed
primarily as audio power out-
put tubes. The power pentode
tubes are used principally as
audio power amplifiers in radio
receivers; however, the power-
type pentode designed for use
in transmitters is gaining
favor, but not for class A am-
plifiers.
480
FIG. 18. Type 47, Plate Characteristics
The first power pentode tube designed for the output system of receivers was the type
47, but it is being replaced by the indirectly heated cathode pentodes such as types 2A5,
42, and 41. The characteristics of the 47, however, are typical of the power pentodes.
The plate characteristics for the 47 are shown in Fig. 18, and power-output calculations
for full grid swing may be made by using eq. (10). The load line drawn through the
operating bias of 15.3 volts at 250 volts on the plate and screen grid represents 7000 ohms
and is approximately the load resistance for maximum power output for full grid swing
and mmjm^rrn distortion. A typ-
ical circuit for the pentode class
A power amplifier is shown in Fig.
19, for the 47-type tube. The cal-
culated power output according to
eq. (10) is approximately 2.4 watts.
Two tubes may be used in push-
pull similar to Fig. 12. The de-
sirable characteristic of the pentode
tube is its power sensitivity, that is,
the ratio of power output per volt
FIG. 19. Circuit for Single Type-47 Audio Amplifier
of signal applied to the grid. This ratio is 3 to 4 times as large as for triodes, but the pentode
power tube has°several peculiar characteristics which are not particularly desirable.
Distortion in. Pentode Audio Power Amplifier. Referring to Fig. 18, it will be noted
that the plate-current increase for a peak grid swing of 15.3 volts (the value of the bias)
is practically equal to the plate-current decrease for the same grid-voltage swing in the
negative direction along the 7000-ohm load line. Therefore, the second harmonic is es-
sentially zero, but it can also be seen that the plate-current change per volt change>tin
bias near the extreme swings of the bias
decreases, which produces a flat-topped
wave. The predominating harmonic in
such a wave is the third, but other har-
monics may be present, their value de-
pending on the flatness of the top of the
output wave. (See p. 5-47.) It is usu-
ally much simpler and more accurate to
measure the harmonic content under ac-
tual operating conditions than it is to cal-
culate it. All the unknown factors, such
as inefficiency of output transformer
and lack of proper plate supply filtering,
are accounted for in the measured val-
ues; their effects are very difficult to de- '
termine and express mathematically.
Experimental curves of percentage dis-
tortion of a 47 tube are shown in Fig. 20.
BIDIRECTIONAL AMPLIFIERS—REPEATERS. All the circuits considered above
amplify in one direction only and will not pass appreciable energy in the other direction.
Power Output- Walls
_O 1-1 ro Q
<&
^
^
\r
I
<
•y£~
~~i
I
V
1
Grid V
Screen
Plate X
Grid S3
Volte
:rts— 16*5
Vofts=250 .
folts=25Q
snaF=15-3
Peak
s
'\
k
V
3 400O 8000 220OO
Load Resistance, rp<, Obese
FIG. 20. Type 47, Output Characteristics
7-14
VACUUM-TUBE CIRCUIT ELEMENTS
West
There are some applications, notably two-way telephony over wires, where it is desirable
to amplify in either direction. (See also Section 17, p. 39.)
Figure 21 shows a schematic diagram of a circuit which amplifies signals coming from
either end of the circuit, line West or East, and distributes the amplified signals equally
between the two lines. Inclosed within the dotted line is a three-winding transformer;
as shown in article 7, p. 6-12, if the proper circuit adjustments are made, energy coming
from either line is divided by the three-winding transformer equally between the input
circuit (connected across
A-B} and the output cir-
cuit (inductively con-
nected). The half enter-
ing the output circuit is
dissipated as heat; but the
half entering the input cir-
cuit is introduced into the
grid circuit of a vacuum
tube through a step-up
transformer and a poten-
tiometer. This is ampli-
fied by the tube, or tubes,
and appears in the out-
put winding of the three-
winding transformer
where it is again divided
equally between East and
FIG. 21. Bidirectional Amplifier
West lines. Thus, although the incoming energy is twice divided, so that only one-
fourth of it is utilized, the power amplification of the tube, or tubes, may easily be several
hundred, so that the net result is a great increase in energy over the original.
The chief practical difficulty with this circuit is that the impedance of lines West and
East must be identical at all frequencies, or energy will be fed by the three-winding trans-
former from the output to the input circuit and the tube will furnish sustained oscilla-
tions, or "sing."
To avoid the requirement of working between similar impedances a circuit such as is
shown in Fig. 22 is used. Here a network of resistors, inductors, and condensers is de-
signed to balance the external impedance on each side of the amplifier. The principle
of operation is the same as above, the left-hand tube amplifying signals entering from the
line West and dividing the energy between line East and the accompanying network (JV) .
Output
Output
Fro. 22. Bidirectional Amplifier with Balancing Networks
Similarly, signals entering from line East are amplified by the right-hand tube and divided
between line West and its network. An impedance unbalance between either line and its
associated network causes some of the energy of the output circuit to be fed by the three-
winding transformer into its input circuit, where it is amplified and fed into the other
transformer. An unbalance here will similarly cause some of the energy to find its way
back through the original path. Thus it is seen that if both lines are poorly matched
by their networks the amplifier may act as an oscillator, but if either line is perfectly
balanced by its network no sustained oscillations will be produced.
CLASS B AMPLIFIERS 7-15
Amplifier circuits of this type are in extensive use by telephone and telegraph com-
panies on their long lines. They are called repeaters,
SUMMARY FOR CLASS A AMPLIFIERS. The foregoing discussion of the class A
amplifiers and the various types of tubes for particular services assumed that the grid
swing or excursions were always in the negative region, and that the amplifier behaved
in general according to the definition of the class A amplifier, as given at the beginning
of this section on amplifiers. There are a few facts about the characteristics of class A
amplifiers which should be kept in mind when designing or studying such devices; some
of them are listed below.
1. The maximum voltage output of a class A amplifier measured at the plate of the
tube is limited by the plate-voltage limitations of the tube and the plate load, r.
2. The maximum power output from a class A amplifier is limited by the plate dissipa-
tion at zero output and the TninJTrmm instantaneous plate voltage for peak positive grid
swing to zero, at which the plate current is approximately double the steady plate-current
value.
3. The load impedance into which the tube must work for maximum power output
is not a simple function of the plate resistance of the tube but depends upon the two
conditions above in cases where the grid swing is not limited. Power-output tubes have
high bias and low plate resistance so that grid swings to zero voltage are not the controlling
limitation.
4. The power output for a comparatively low and limited grid swing, that is, when
limitations of 1 and 2 are not effective, is maximum when the load resistance is equal to
the plate resistance of the tube. For this same grid-swing limitation, the maximum out-
put voltage or gam approaches the amplification factor of the tube as the load resistance,
r, increases toward the value of the tube plate resistance, rp.
2. CLASS B AMPLIFIERS
GENERAL. Because of the relatively low power output of class A amplifiers and the
fact that the plate dissipation is maximum for no-signal conditions, the overall efficiency
of such an amplifier is very low. In applications where considerable power is desired either
at radio or audio frequencies, the size of the tubes and the cost of plate power supply, per
watt output for class A amplifiers, increases so rapidly that such amplifiers are not used.
In the broadcast receiver it is not economical to obtain power outputs greater than about
5 or 6 watts without resorting to class B amplifiers or some combination of the class A
and B amplifiers.
The grid swing in the class A amplifier is usually limited to the negative region for the
entire input cycle because, in general, grid swings into the positive region result hi plate-
current distortion, chiefly because of the large external grid circuit impedance and limita-
tions in plate-current swing.
According to the definition of a class B amplifier, the bias is such that the operating
plate current is small, so that for the no-signal condition the plate dissipation is low.
Therefore, the grid swing in general is limited only by a non-linearity of plate current
and grid voltage when the grid swings positive from the operating point. Almost any
three-element tube and some pentodes may be used in a class B amplifier. However,
some tubes are to be preferred for reasons that will be evident after the various calcula-
tions are made from the various sample tube characteristics as shown and discussed
below.
LOW-POWER AUDIO AMPLIFIERS. Since self-bias, as obtained in a pushpull
circuit as shown in Fig. 12, depends upon the signal (because the average plate current in a
class B amplifier depends upon the signal) and since there is no other convenient means for
supplying fixed bias in the usual receiver, low current at zero bias is very desirable in tubes
for use in class B amplifiers. The plate characteristic curves for such a tube are shown
in Fig. 23, with the corresponding grid currents for various grid voltages plotted against
plate voltage. Experience has indicated that a plate load resistance of about 2000 ohms
for this tube with 400 volts on the plate is approximately the optimum value for power
output and plate-circuit efficiency. The 2000-ohm load line is drawn through the operat-
ing point to obtain data for power-output calculations and grid-current values to deter-
mine the input resistance of the grids. Data can be obtained from this set of curves to
replot curves of plate current and grid current against grid voltage, which are more useful
for performance calculations than the curves in Fig. 23. Such curves are commonly
called dynamic transfer characteristics.
The data for these dynamic transfer characteristics may be optionally taken directly
from meter readings in a circuit such as shown in Fig. 24. Here are plotted various curves
7-16
VACUUM-TUBE CIRCUIT ELEMENTS
for different load resistances. Except at points near the zero bias axes, that is, for a grid
swing of about 5 volts, these curves represent the dynamic performance of the 46 tube for
various load resistances for one half-cycle. Another, similar tube is connected in pushpull
' 200 i
360 400 44Q
FIG. 23. Type 46, Plate Characteristics
in order to supply power for the other half-cycle. If the two tubes have similar character-
istics and the pushpull input and output transformers are well balanced, the output wave
will be symmetrical and only odd harmonics will be present in the output for a sinusoidal
input wave.
The power-output calculations for the 46 from the curves in Fig. 24 are made like the
power-output calculation for the class A amplifier, except that the plate current Imax
(the peak plate current read from the curves) is the total change in plate current from the
operating point of essentially zero plate current. Since Jmax is the peak value of the out-
put wave, and if little distortion is
present for sinusoidal inputs, the power
output for the two tubes is 72max^/2.
The average plate-current input for
two tubes at a constant plate supply
voltage, JSb, for approximately full power
output is /maxS/T = 0.637Imax- Since
the plate voltage is constant the power
input to the plates of the two tubes is
0.637Imax JEb. Therefore, the plate effi-
ciency is
"•"•-rig <»?
and the plate dissipation per tube is
PL loss =
- 0.5/2maxr
(17a)
-10
+10
H-20 4-30 +40
Grid Volts
+50 +60 +70
FIG. 24. Type 46, Dynamic Transfer Characteristics
The maximum theoretical efficiency
is obtained when the peak a-c plate
voltage is equal to the d-c plate volt-
age and, according to eq. (17), is 78.5
per cent.
The above equations are quite accu-
rate at full or nearly full grid swings;
the accuracy decreases with lower grid swings, the decrease in accuracy being a function
of the no-signal or standby plate current. For the theoretical condition for a class B
amplifier of zero plate current at no signal, they are accurate for all grid swings.
CLASS B AMPLIFIERS
7-17
If the maximum value of plate current is taken from the curves in Fig. 24, for the
2000-ohm load, sample calculations are as follows:
0.1502 X 2000
= 22.5 watts output
0.637 X 0.150 X 400 -
0.150 X 2000
1.27 X 400
0.1502 X 2000
59 per cent plate efficiency
7.9 watts plate loss per tube
It should be noted that the load resistance used is the resistance the tube works into
during the half-cycle it functions so that the plate to plate equivalent load on the primary
of the output transformer is 4r.
INPUT RESISTANCE. The non-linear grid current in class B amplifiers for audio
frequencies is a principal difficulty to overcome. The plate-current grid-voltage curves,
as shown in Fig. 24, are for perfect regulation of grid voltage or the equivalent of zero
resistance in series with the grids. An essentially zero input resistance to the grids,
however, is not practical to attain, but values can be obtained which are quite low com-
pared to the minimum instantaneous resistance of the grids of the class B amplifier tubes.
The slope of the grid-current curves in Fig. 24 at any particular grid voltage gives the
instantaneous input resistance of the amplifier. The niinimum value of the grid resistance
occurs at a maximum grid swing of about 45 volts positive. The slope of the grid-current
curve at this point represents approximately 500 ohms, while at points below 45 volts
on the grid, the grid resistance is about 1600 ohms, and at near the zero axis, the resistance
is still higher for each tube. However, the grid current is not zero at zero bias, so that
the input resistance of the two tubes over the region at which grid current flows to each
tube is the resistance of the two tubes in parallel. Therefore, to drive the grids of two
46-type tubes properly as audio amplifiers, the amplifier stage supplying voltage to the
grids of the 46's works into a load resistance of approximately 4500 ohms for each tube,
or a combined resistance of approximately 2250 ohms for a short period during which
each tube draws grid current. When one tube ceases to draw grid current, because its
grid is too negative, the input resistance rises very rapidly to approximately 4500 ohms,
after which it decreases gradually to 500 ohms.
Because of this erratic change of input resistance to the 46's as class B audio amplifiers,
it is very important to keep the equivalent impedance in series with each grid a minimum.
The low-impedance requirement is met by using low-plate-resistance driver tubes, prefer-
ably in pushpull with a transformer step-dawn ratio as great as the plate-voltage swing
of the driver tubes will permit; also the coupling transformer leakage reactance and
resistance must not appreciably affect the impedance in series with the grids.
The input requirements may best be understood by referring to the circuit for a class B
audio amplifier shown in Fig. 25, with the various equivalent circuit constants inserted.
4-275 +400
FIG. 25. Circuit and Equivalents of a Class B Audio Amplifier
The combination of tubes shown is perhaps the most practical combination for power out-
puts of approximately 25 watts. The transformer T is merely an interstage voltage trans-
former to supply audio voltage from the source to the grids of the type 45 tubes as class A
amplifiers. For the grid and plate voltages as shown, the peak plate-voltage swing is
approximately 165 volts each side of the operating point for load resistances of the order of
10,000 ohms, which would be a peak voltage of 330 volts on the primary of transformer T.
Since according to Fig. 24 the grid swing for the 46 tube, for full output of about 25 watts,
is approximately 55 volts, the ratio of the transformer TI is the ratio of 330 to 55 or 6 to 1,
as measured from plate to plate of the driver tubes to each grid of the 46 tubes. This
transformer has an impedance ratio of 36 to 1. The plate resistance, rp, of the 45 tube
is approximately 1800 ohms per tube so that the equivalent resistance in series with the
7-18
VACUUM-TUBE CIRCUIT ELEMENTS
primary of TI is 2rp, or 3600 ohms for the above case. Therefore, the equivalent resistance
in series with the grid of each 46 tube is (in addition to transformer losses)
(Turn ratio)1
= n = 100 ohms
(18)
The actual impedance is usually about 10 per cent higher than the above calculated
value because of transformer losses, but such losses are usually allowed for by assuming a
grid swing about 10 per cent or more higher than the actual swing needed for a given
power output. In addition to the equivalent resistance, TI, in series with the grids of the
46 tubes, there is an equivalent inductance, LI, which is the equivalent leakage reactance
in series with one side of the secondary of transformer TI. As explained above, the change
in input resistance of the 46 tube is very rapid over certain parts of the audio cycle which
results in current flow to the grids at harmonic frequencies much higher than the funda-
mental frequency. The frequency at which these grid currents flow may be 5 to 10 times
the frequency of the fundamental, depending upon the frequency and amplitude of the
signal. With currents flowing at such frequencies to the grids of the 46's, it is evident
that the equivalent inductance in series with the grids due to leakage reactance of the
transformer TI must be low in order that the grid voltage at these frequencies will be
low. A high leakage reactance in the input or driver transformer manifests itself in the
form of a fuzzy or a ragged output wave over certain portions of the cycle, and it may
cause very high transient voltages in the plate circuit, which are responsible for many
output transformer breakdowns and the tube failures.
OUTPUT CIRCUIT REQUIREMENTS. Assuming a low-impedance circuit to the
grids of the 46's, which results in very little distortion of voltage supplied to the grids,
there is still a source of distortion in the
plate circuit because of the deviation of the
plate-current curves from a straight line.
This deviation is shown in Fig. 24, and if the
points about the zero axis are plotted on a
much larger scale and the slopes of the two
plate currents added over the period during
which plate current flows to each tube, it
will be found that the per cent deviation
is perhaps greater at zero than at any other
point. In the 838 tube which was specially
designed for class B operation there is appre-
ciable plate current at no-signal condition;
FIG. 26. Distortion Curves for RCA 46 Tubes as however> *}* ^ 0* th* Plate"current
Class B Audio Amplifiers curve 1S such that when tw° tubes are oper-
ated in pushpull the resultant output current
is practically linear. This characteristic of the 46 may be seen by referring to the results of
distortion measurements (Fig. 26) as made on an experimental amplifier with constants
approximately as shown in Fig. 25. The non-linearity near the zero signal is distinctly
shown by the rapid rise of the third harmonic at about 1-watt output, after which one
tube ceases to work for most of a half-cycle, resulting in a partial balancing out of the
third harmonic for certain power outputs.
From the definition of the class B amplifier, and from eq. (17), it is evident that the
plate current to the class B audio amplifier tubes is approximately proportional to the
grid excitation and that the efficiency increases to a maximum at full output. Referring
to Fig. 24, it is seen that, if the plate voltage decreases because of poor regulation of the
plate supply, the peak plate currents will not be reached as indicated by the curves.
Therefore, the plate supply voltage should have good regulation and should be by-passed
well for instantaneous peak plate currents. (See p. 7-108.)
The shape of the plate current curves in Fig. 24 cannot be used to calculate distortion
by the simple formulas given above for the second and third harmonics. The fact that
the output resistance from the driver stage is about 20 per cent of the grid resistance at
near the peak swing alters^ the plate-current curve appreciably at the upper limits of
plate current, which complicates the mathematical determination of harmonic outputs.
Because of the complicated nature of the procedure in calculating harmonics, it is 'much
easier and more accurate (for small amplifiers) to analyze the output wave, from an ex-
perimental amplifier including the driver, for harmonics by means of a reliable voltage
analyzer.
LIGHT-WEIGHT CLASS B AUDIO AMPLIFIERS. Because of the high efficiency
of the class B audio amplifier its use is very desirable in a battery receiver, in an automo-
bile receiver, or where space and weight" are limited. The use of small tubes for a given
8 12
Power Output - ^
24
CLASS B AMPLIFIEES
7-19
power output is represented by a miniature 6AU6 driving a single 1635 class B output
tube. The output power from this combination is of the order of 12 to 15 watts audio
power with low distortion and with very low plate drain by both the driver and output
tubes.
As explained above, bias for a class B amplifier is difficult to obtain and keep constant
because of the summation of grid-current and plate-current peaks that must flow through
a self-bias resistor and because of the grid-current peaks if a separate bias is used. There-
fore the 1635 tube was designed for zero bias at a maximum of 400 volts plate supply.
A 4000-ohm load line may be drawn through a point at zero bias and 400 volts supply
to the plate on a family of published plate characteristics for the 1635. The dynamic
transfer characteristics are shown in Fig. 27 for a 4000-ohm load resistance. The grid
+90
-90
35 -30 -25-20 -15 -10 -5 0 +5 +10 +15 +20 -4-25 +30 +35
Grid volts
FIG. 27. Dynamic Transfer Curves for a 1635 Tube as a Class B Audio Amplifier
current vs. grid voltage is also shown in Fig. 27. A careful examination of the plate-current
curve in Fig. 27 will show that the current is quite low at zero bias but trails out before
cutoff similar to a variable-mu tube.
At zero bias about 6 ma plate current flows to each plate so that each plate contributes
to the output. Since the plate resistance of the 1635 is high the output power from each
plate is measured by plate-current deviation from its zero value through the load resist-
ance. In pushpull operation if the plate current of one tube is increasing the other is
decreasing, and since the phase of the currents is reversed in the output transformer the
output current is given by the difference in plate current to the two plates. The true
output-current curve is then obtained and plotted in Fig. 27 as the resultant output cur-
rent. This resultant-output-current curve is more nearly linear for the 1635 tube than
for other double tubes because of the special grid construction. Because of the special
grids the grid current at zero bias is lower so that the sum of the grid resistance of the two
tubes is higher than for other double plate tubes during the time grid current is flowing
to both grids. This higher input resistance to the tube for small signal swings reduces so-
called high frequency or "fuzz" type of distortion.
7-20
CIECCJIT ELEMENTS
At « rrawentathr* P^k plate current of 80 ma in Fig. 27 the output is 7*Bi»/2 ! - 12.8
w.t*/ ThT^nd «ak^g is +32 volts for the above peak plate current, and the grid
™Js ^a 52. These peak grid values of current and voltage ^permit the driver
i* The slope of the grid-current vs. grid-voltage cune at +30 tc ' +3- volts
a • Stance of 500 ohms, increases to about 1500 ohms at about +6 volts on
d and dm^M again to about 700 to SOO ohms near the zero axis because of grid
*irids. The above variation of input resistance necessitates a
of the OAU6 pentode to be used as a driver is Quite high so that
is used to Iow0r its output resistance. The circuit for the 6ATJ6 driver and
the 6AU6 under the voltage ^onditions
shown in Fig 28 it will be seen that the bias for class A operation is about 1.5 volts at a
plat* mrrent of about 7 ma. At double plate current and a signal swing to zero bias the
plate *winf> w about 225 volts. A peak swing of about 32 volts is needed on the grids of
Uie 1635 BO that the step-down ratio of the driver transformer to each grid is about 7 to 1.
6AU6
1635
-f-300 - -{-150 +400
Ft©, 38» Drir«r and Output Circuit for a 1635 Class B Audio Amplifier
maximum mi-rent output from each side of TI is then 7 ma X 7 — 49 ma, which is
than mm pie driving capability for a needed peak grid current of 25 ma. As noted
above, the variation of grid resistance or load on T\ was 500 ohms to about 1500 ohms.
Hit input roristance should be as low as 10 per cent of the minimum grid resistance to
keep the input distortion to & low value.
Thi? gm of the 6A1T6 is about 5000 micromhos, and, if it is assumed that 1 volt peak
were applied to the plate of the 6ATJ6 and that 0.2 of a volt peak gets back to the grid of
til© 6A176 t^mi^a Jfc, tfae effective output impedance of the 6AU6 to one side of the
1 1000
m (Ratio of m«
Tfe« eff«ciir® imter^J rc^taaee of the transformer, TI, to each side of its secondary
may be about 20 ofams fw a good design so that the total input resistance in series with
1635 grids m alxmit 40 ohms. This low value of resistance will effectively reduce input
to a low vata*.
|%. 28 id the combined plate resistance of Vi, jRs, and fij is 50,000 ohms,
J£i in tJb® afe®*r« <^lmla4i(m« for feedb&ek voltage will be 200,000 ohms. Therefore, 20
par cemt 01 the peak plate swing of 225 volts on the plate of the 6AU6 will require about
1 ma of taw 6AtTt plate-atrreut peak swing and apply 45 volts audio on the plate of the
la tliis emse Ft EIU^ sup^y au equivalent voltage of 45 volts at its plate to
out ^e Iwdlsaek v^tag® P*«s a peak voitage of about 2 volts to drive the grid
k>**i M 400© ofeiaa per plate the plate to plate load for Tz is 16,000
I m^sfc Iiave tow leakage reactance to prevent fuzz-type dis-
rtkiFig.25. A cliecic of constants for the 6AU6 as a degenerative
fa*dfca«fc «var far taw 46*1 in Fig. 25 indieal©s tfeat tlie 6AU6 ^ essentially as good a
4r*fw m or b«t««r 4^® Ow two 45T$. This indicates the effectiveness of the addition of a
•atdfcark res^w ^ » F%. 2S,
S^ssf ^«pa«3ri^ioti nmy b« f«d b«^ from a resistance divider, R^ across the output of
Fj t*» tht <«taodt «i ^ a« ^)wa in F%. 2S to ^crease tfe© distortion of the system further
Th» totort»a vt, ©utfmi pow^- of tbe «ira«ifc dk^ro ia Fig. 2S is shown in Fig 29 The
CLASS B AMPLIFIERS
7-21
feedback for the overall distortion curve was an amount required to reduce the overall
gain about 2 or 3 to 1.
Other sharp cutoff pentodes such as the 6SJ7 may be used as drivers. Battery tubes of
the 1.4 volt series may be used in combinations to obtain high outputs for given input
powers.
s 400 volts
4000 ohms
6 8 10
Power Output, Watts
14
16
FIG. 29. Overall Distortion of the Circuit of Fig. 28 Using the 1635 as the Output Tube
MEDIUM-POWER AUDIO AMPLIFIERS. A set of curves similar to the curves in
Fig. 24 is shown for the UV849 tube in Fig. 30. It will be noted from these curves that
the class B operating bias is approximately — 140 volts and that the instantaneous slope
of the grid-current curves is positive and negative with magnitudes as low as 500 ohms.
Considering the relatively high grid voltages at which these low instantaneous grid re-
sistances occur, these tubes are hard to drive without appreciable distortion. However,
two UV845-type tubes operating at full rated voltages may be used to drive these tubes
successfully with an equivalent resistance of approximately 100 ohms in series with the
grids of the UV849 tubes.
1400
+40 +80 +120
FIG. SO. Dynamic Transfer Characteristics of 849 Tube
-160 -120 -80 -40 0
Grid Volts
By applying eq. (17) to calculate the various powers from data obtained from Tig. 30,
it is found that the maximum power output for the 2500-ohm load line is about 1350
watts for two tubes, the plate loss is about 350 watts per tube, with a plate-circuit efficiency
of approximately 55 per cent. These calculations do not take into account the transformer
losses. Such audio power outputs are used principally to plate-modulate a class C radio-
frequency output amplifier.
HIGH-POWER AUDIO AMPLIFIER. The 500-kw broadcasting transmitter operated
at WLW in Cincinnati, Ohio, used high level modulation with a class B audio amplifier
capable of approximately 325-kw audio output power. At the time this station was first
operated, early in 1934, it was the world's largest broadcasting station. The class B
amplifier for the above station used eight type-862, 100-kw tubes, with 12,000 volts on the
As stated above, tubes other than the ones discussed may be used as class B audio
amplifiers, but their particular grid characteristics must be known in order that a driver
system may be properly designed. The load resistance and plate-current characteristics
are also important items to consider in the design of a satisfactory class B audio amplifier.
RADIO -FREQUENCY AMPLIFIERS. The class B radio amplifier functions much
the same as the class B audio amplifier as far as the grid currents and plate currents are
concerned, except that the plate-current distortion may be greater with a correspondingly
higher output power without serious signal distortion. This is because the second and
higher harmonics are multiples of the radio frequency and are outside of the frequency
range of interest. The principal difference between the two amplifiers is in the input or
driver circuits and the output circuits. If the input or driver circuit is tuned, the har-
monics are by-passed and do not appear on the grids, which results in a well-regulated or
low-impedance driver source, as far as the fundamental frequency is concerned. As in the
class B audio amplifier, the regulation of the voltage to the grids of the class B tubes de-
pends upon the ability of the driver tube to supply the instantaneous grid currents directly.
Another factor which reduces distortion to a negligible value is the fact that the plate
circuit is timed; thus it will absorb the fundamental component of the plate current and
by-pass the harmonics. The power output of the class B radio amplifier may be cal-
culated like the power output for the class B audio amplifier if somewhat greater peak
currents are assumed for peak outputs. It would seem from the above that the class B
radio amplifier, also known as the linear amplifier, is inherently a simple type of amplifier
to design; this is true if it is desired only to obtain a power amplification of the funda-
mental frequency. However, it is not economical to use such an amplifier as merely a
tuned amplifier for voltage or power amplification, because in such cases the class A
amplifier would probably be better for voltage amplification and the class C amplifier for
power amplification. The real use for the class B radio amplifier is in circuits where a
low-powered modulated signal is to be amplified to a higher power level. Referring to
the definition of the class B amplifier, one characteristic of the amplifier is that the output
voltage is proportional to the input voltage; therefore, if a modulated radio-frequency
signal is used to excite the grids of a class B radio amplifier, the output for an ideal case
would be a modulated signal identical to the modulated input signal, except that it would
be at a much higher power level. The increase in power level is 20 to 100 times, depending
upon the degree to which the amplifier is driven.
A typical circuit for such an amplifier is shown in Fig. 31, in which the tuned input
circuit LiCiCzCs is so arranged that C% equals Cz and each has a value with respect to
Bta-s far Approximate^*1
Plate Current Cufcotf
FIG. 31. Circuit for Class B Radio Amplifier
Ci that permits the desired grid swing of the tubes, Vi and 72, for a given modulated sig-
nal applied to the input circuit. Inductances L2 and L3 are radio-frequency chokes to
provide a low d-c resistance path for the grids, and rx and rz are resistors from the grids
to ground to suppress undesirable oscillation. C6 and C7 are neutralizing condensers,
and the output tuned circuit is LtdCs, in which C4 and C5 are equal. The radio-frequency
choke 1/5 provides a floating center tap for L4 because the tuned circuit is center-tapped
in the condenser branch. The circuit as shown is for a pushpull class B radio-frequency
amplifier, but, as stated above, a single tube may be used in a circuit similar to the one
discussed, by leaving out the unnecessary parts or sections of the circuit. The type of
circuit shown, or its equivalent, was in common use in most broadcasting stations of 1000
CLASS B AMPLIFIEKS
7-23
watts or more. However, the present trend is toward the use of the more efficient high
level modulation system. (See p. 7-74.)
Distortion. As discussed above, there is little distortion from a tuned input and tuned
output amplifier as far as the fundamental radio frequency is concerned. Since the prim-
ary use of the linear amplifier is to amplify modulated signals without distortion, the
linearity of the amplifier becomes a factor which determines almost entirely whether the
demodulated output is distorted or not. The linearity of such an amplifier is determined
by the ratio of output current, or voltage, against rms input voltage. The curves of
Fig. 32 are plotted from actual experimental data obtained on two RCA 846 tubes in
pushpull as a class B radio or linear amplifier with 7500 volts on plate. For a bias of
— 150 volts, the output tank current is approximately linear with respect to the grid-
excitation voltage from zero to about 4 amp. If the amplifier is used as a radio-frequency
output amplifier in which the input signal is 100 per cent modulated, the normal output
'
E& g=s 7BOO Vblts
- r=6000 Ohms per Tube -
Output Resistance =» 374 Ohms
400 6OO 800
R,P. etfd Volts perTobe CR.M.S.)
FIG. 32. Characteristics of RCA 846 as Class B R-f Amplifier
tank current would be approximately 2 amp, which corresponds to a grid excitation of
470 volts for approximately 1300 watts output. It will be noted that such high per cent
modulation of the excitation voltage in this case causes a deviation from a straight line
at both the upper and lower limits of swings so that the predominating harmonic in the
demodulated output signal is the third. If a lower bias is used the curve would be more
nearly linear from the operating point of 2 amp, but the slope at the upper end would be
approximately the same resulting in a second harmonic for 100 per cent modulation.
The flattening of the output tank current near the zero axis, for the curves in Fig. 32,
is due to the large bias chosen; however, the flattening of the upper end of the curve
may be due to emission or space-charge limitations which limit the peak plate currents.
Another factor that often contributes to the flattening of the upper end of the output
tank current curve is the inability of the modulated exciter to supply the higher value
of average grid current without distortion to the output tubes at the peak values of grid
excitation. The driver must have low impedance to the grids of the output tubes to
prevent distortion, for practically the same reasons as a low impedance is required for the
input to the class B audio amplifiers.
Since the normal carrier value of output current for the class B radio amplifier is
approximately one-half the peak value and occurs at one-half the peak value of grid excita-
tion, it can be seen from eq. (17) that the efficiency of the plate circuit is relatively low.
(See p. 7-17.) This efficiency is usually 20 to 30 per cent. The carrier power output is
only 25 per cent of the peak power output; therefore, except in tubes where peak plate
voltage or peak plate power input is limited, four times as many tubes are theoretically
required for class B radio amplifiers for a given power output as are required for a class C
high level modulated radio-frequency amplifier. Actually the water-cooled tubes are
limited by peak plate voltage for the plate modulated class C amplifier so that the number
of tubes for a class C amplifier, when these tubes are used, is approximately one-half that
required for a class B radio amplifier.
7-24 VACUUM-TUBE CIRCUIT ELEMENTS
SUMMARY IOB. CLASS B AMPLIFIERS. Some of the more important require-
ments to meet in the design and operation of class B amplifiers and some of their charac-
ter istk$ may be summarized as follows.
1. The rapiit system to the class B audio amplifier must have low impedance, especially
iC the instantaneous values of grid current change rapidly either negatively or positively.
The dbp© of the grid-current curve or its rate of change per volt applied to the grid is the
grid mastaoe at the point taken. The equivalent inductive reactance in series with
each grid because of driver transformer leakage is a part of the impedance in series with
the grids; it must be kept very low if the instantaneous values of grid resistance are low
aad change rapidly over the audio cycle.
2. Failure to meet the low-impedance input requirements usually results in appreciable
distortion, and generally the output transformer is subjected to high peak voltages which
may damage the transformer or the tubes.
3. The load resistance the tube works into is one-fourth of the calculated plate to plate
impedance of the loaded output transformer. This applies to radio-frequency as well as
audio-frequency amplifiers.
4. The load line for the class B amplifier for radio and audio frequencies should be as
high a resistance as possible consistent with grid current peaks and space-charge limita-
tion in order that the plate efficiency may be maximum. Somewhat higher peak plate
currents may be assumed for the class B radio amplifier, because of the tuned plate
circuit,
5. The class B audio amplifier is the most efficient type of amplifier for audio fre-
quencies, and may attain a plate efficiency of 65 to 70 per cent at full output power for
some of the larger tubes.
0. Hi® dase B radio amplifier has poor plate efficiency, which is usually 20 to 30 per
eeat, so ihsA a rel&ti'roly liigh tube power capacity is required for a given output.
7, Tbe ciaas B radio amplifier also requires a well-regulated or low-impedance driving
scmr«je, but the re<|uir«Daents are not as strict as the driver requirements of the class B
audio amplifier, because the radio amplifier may have a tuned input circuit,
S» The plate supply for the class B audio amplifier must have good regulation, espe-
cially if tubes witfe higa bias are used. The plate supply regulation is not so important
with the class B radio amplifier because the average plate current is essentially constant.
Btifficieiit plate supply by-pass capacitance is necessary in either amplifier to maintain
constant plate voltage over the audio cycle.
3. CIASS C AMPLIFIERS
GENERAL. Th® class C amplifier by definition is an amplifier that is biased con-
s«teraMy beyond plate current cutoff, so that plate current flows for a period less than
!$@ electrical degrees* during the time the grid swings in a positive direction from its
twraud v»ls*& of bias potential. In general, the grid is driven to the point of saturation,
thftt 15, to a. point m& wfeieti the output voltage is no longer proportional to input voltage.
Uncles- tlo» 0®ndffcitM the efficiency of tlie amplifier is approximately maximum for any
gjifTMa piAtft^-ciresiBt conditions, the output voltage is proportional to the d-c plate voltage,
and ike oatpat power is proportional to the square of the d-c plate voltage.
Bm&e* in gMMral, appreciable power is required to drive the class C amplifier because
of tli® rdtowiy tai«Ji positive grid swings, this type of amplifier is essentially a power-
atsiptifier dwnm. Because of the distorted plate current that flows during only a part
of & Imlf-cyelfe H m uteessary to tuae the output or plate circuit of the amplifier if- an
B®«te0rt*d output WVF® is tiesred. Therefore, the class C amplifier is essentially a
«t^»-irftqiiw<^ amplifier aad is used as the output device for radio telegraphy or high
3*w4 Eaoduiat*d tetephony transmitters.
CIBCIHT CALCULATIONS, Since the class C amplifier can be used only as a tuned
pi wfe*r$ distortion of the output wave is permitted, it is obvious that
Ms ampliSer M nmefe more limited taan the applications of the class A
m wsapiiiwrs. Im Hie dbas C amplifier it is diScuit to predict the performance of
ftwail»^»t^«i«racl«rWcs. As long as the plate circuit load, r, has a sufficiently
t© limit the miaimiim ia^miaaeoiK plate voltage to a value such that the
9M*» aimo* m «**nti«J}y ^|f sine waves, ike power output and other characteristics of
WftOTOHt wd tote may be eafcmlaied la mudi the same manner as for the class B audio
Hw»w, umW these conditions, the piate-drcuit efficiency is usually less
«mt. Wtai th* load msstaace is high tbe minimum instantaneous plate
****^ *rs*WW3sfii •** » th«* essentially no plate current can flow at the
, **K-*U-*> th* pfcto Y^t^ » ^s»r aero.
CLASS C AMPLIFIERS
7-25
To illustrate better the above features of the class C amplifiers as well as the general
circuit features, it is well to discuss the typical class C amplifier circuit such as shown in
Fig. 33. The proper constants to use in the circuit depend upon the tube used, general
class of service, and the values of maximum grid and plate currents allowed. For the
204A tube the maximum allowed constants are: d-c plate voltage, 2000 volts; d-c plate
current, 275 ma; plate dissipation, 167 watts; d-c grid current, SO ma.
If a modulation factor of 1 is applied to the plate voltage, it is evident that at peak
upward modulation the instantaneous plate voltage will be 4000 volts. In order that
plate current cutoff may be obtained at 4000 volts on the plate, so that the tube may
continue to operate as a class C amplifier at this voltage, the bias required is approximately
— 200 volts, but a bias somewhat beyond plate-current cutoff, such as —250 volts, should
be used. Therefore, since the allowable direct current through the bias resistor, rjT of
Fig. 33, is a maximum of
SO ma, a voltage drop of «JL
250 volts requires a resist- • — L-
ance of 3125 ohms for TI.
The power dissipated in
n is approximately 20
watts, and the power dis-
sipated on the grid of
the tube is comparatively
small because of the low
resistance of the grid when
the grid current is large.
FIG. 33. Typical Circuit for Class C Amplifier
If it is assumed that one-third of the bias power is dissipated on the grid, the total power
required of the r-f input circuit is approximately 30 watts.
This power must be supplied by the exciter amplifier, and the loss in the resistor TI
cannot be supplied by means of a separate voltage supply in the hope that the exciter
is required to supply the grid losses onlj-. The grid-leak method of supplying bias as
shown is a self-biasing arrangement and consumes no power from the plate supply. The
one disadvantage of this method of supplying grid voltage is that if the excitation is lost
the class C tubes have no bias, so that, in the case of the 204A, the resulting plate current-
would cause excessive plate dissipation. This difficulty may be removed by using a com-
bination of a fixed bias (or biasing resistor in the cathode to negative plate supply lead)
to limit the plate current if the excitation is lost and the additional bias supplied by a
leak system as shown.
The input circuit to the tube is tuned and the inductance, LI, is center-tapped in order
that the amplifier may be neutralized by means of the condenser Cs. The plate circuit
is tuned by means of €4 and La, which in turn is coupled to an output circuit. The output
circuit reflects, to the C±Lz circuit, an equivalent resistance of 2r across the tuned circuit.
Therefore, r is the approximate resistance the tube works into during the time plate cur-
rent flows.
POWER CALCULATIONS. The efficiency of the plate circuit of the class C amplifier
can be estimated quite accurately if the peak a-c voltage across the tank circuit C^L*
is measured and used in eq. (17), as for the class B amplifier, provided the plate current is
approximately one-half sine wave or that the fundamental component of the current is
very large compared to the harmonic components. For this case it will be seen that the
expression /max ?" is in reality the peak a-c voltage measured across the plate tank circuit
in which Jmax is the peak value of the fundamental component of plate current and r
is the value of resistance the tube works into during the time plate current flows. The
values of Jmax and r are more or less fictitious, but their effective product is approximately
the measured peak plate voltage.
Referring to the ratings on the 204A as given above, the permissible input plate power
is 550 watts with only 167 watts plate dissipation, which requires a plate efficiency of
approximately 70 per cent. Therefore, from eq. (17), it is found that the peak voltage
across the tank circuit is 1778 volts. This peak voltage leaves only 222 volts on the plate
to cause the peak plate current to flow. The power output for the above power infmt and
plate loss is 383 watts, and if the peak plate voltage swing is 177S volts, as calculated
above, the approximate value of 2r is found to be 4150 ohms, which is tbe eqtuvaieiit
load resistance across the plate tank circuit, and the resistance the tube works into is r,
or approximately 2075 dims. The peak value of the fundamental component of plate
current, as found from the expression for peak a-c plate voltage, is 860 ma. It is doubtful
if this value of plate current Sows at the instant the plate voltage readies a roinmmm
vahie of 222 volts. However, plate-cimiit efficiencies of 70 per cent are easily attained,
so that, even though the actual plate current may be considerably below S60 ma at the
7-26
VACUUM-TUBE CIKCUIT ELEMENTS
instant the plate voltage is 222 volts, the peak value of the fundamental component may
be SaO ma without sw^dent plate-current distortion to affect the plate loss seriously.
Exmmtic*? has shown, however, in experimental class C amplifiers that approximately
70 to 75 per cent piat«s-tirciiit efficiency, for a circuit as shown in Fig. 33, is the limit of
efficiency, because the actual plat® current for higher load resistances deviates so far from
a half sine wave of current at higher peak values of a-c plate voltage that the plate-current
tjanaonic! Icwae* increase to keep the plate efficiency at a more or less constant value, in
«©!** &f the f*<* that the measured peak a-c plate voltage increases.
EPSCUU, FILTER FOE HIGH EFFICIEHCY. Equation (17) indicates that if an
«3aeati*l!y feaH we wave of plate current can be caused to flow to the plate the efficiency
mmy *» <^n»eci to increase as the peak tank \-oltage increases.
When tfe* P«»k *»«* voltage approaches the plate voltage the efficiency by eq. (17)
emrmxfam 78.5 per cent. If the peak plate voltage could reach 1,27 times the d-c plate
voltage, the efficiency would be 100 per cent, provided that the plate current is essentially
a half ^m wave and the plate resistance of the tube during the time current flows is^zero.
This 100 per cent efficiency condition is impossible, of course, but the limit of efficiency
is flee* to be 100 per cent, because the plate circuit is tuned and filters may be inserted in
news with the plat« to prevent appreciable flow of harmonic plate currents. Such a
filter circuit is shows in Fig, 34. The inductance L* is comparatively large and offers a
high impedance to the fundamental and har-
monic plate currents. The primary function
of LI is to provide a path for d-c plate cur-
rent but to offer a high impedance to all a-c
components of the plate current. The induct-
ance In and capacitance Cs are tuned to
series resonance for the fundamental fre-
quency of the circuits. Therefore, the band-
pass filter offers low impedance to the funda-
mental component of plate current but is
designed to offer high impedance to harmonic
components of the plate current.
The value of tfee more or less fictitious plate resistance is a function of the tube and its
evfHwtkm, and it may be calculated if ail the constants of the tube and circuits are known.
Howtwr, an apparent resistance of the tube may be easily calculated from the plate
efficiency. This is done by assuming that the apparent load resistance is in series with
an apparent plate resistance that will give the measured or calculated plate-circuit effi-
cieacy.
Such a formula is given below:
Circuit for Iiaereased
Data C Amplifier
— .
— 2r
apparent plate resistance
(19)
in wMch 2r is the equivalent resistance in parallel with the tank circuit due to the load
aoiaiiertecl to the class C araplilier. Since the tube functions for approximately one-half
tJbe tine* th® actual effective resistance of the tube is approximately one-half of the ap-
parent neiistaiHse ?*&, and the load the plate works into is one-half the equivalent load
ikee or r. The load resistance r as calculated for the 204A at rated conditions as
atxrre is ^07S ohms, and the calculated efficiency is 70 per cent. Substituting these
i in formula <lf)t the effective resistance of the 204A is about 890 ohms.
If the harm«mie coropofwjnts o€ the plate current are to be effectively reduced, the im-
peskufje ©f the draft -W*r*, when tuned to the fundamental frequency, must be 4 or 5
twaes the approximate e&eetiv© resistance of the tube at the second harmonic of the funda-
mwrta! fntqpMmx* Tbe impedance to higher harmonics, of course, will be still higher.
TliwdbTt, a ttmgh approximation of what the impedance of the filter should be at the
•MMMl imn«*©i8ie m «*|mal to the normal effective resistance across the output tank circuit
Kfc M power output of the tube.
S^^i imp^iinw at the second tmrasonic frequency necessitates a comparatively large
I* t» C m&® lor the series toned circuit £4C&- Since the a-c component of plate current
iwiMft «lra*fr this ieries &in*d circuit, tlie voltage across Li and C6 reaches quite high
wiiMB M the fmii4»3s*i*fea] fre<t*iesey, and tis^e voltage across L3 at all the harmonic frequen-
cies M «onp«rtttiTriy fa^s. However, the system permits approximately only half sine
waeis erf pb*« curmst at tfe« teidameiital frequency so that high efficiency can be achieved.
is» type «£ filler Isa® be*s succsessfuily xtsed to increase materially the efficiency of a
«C Mttplifiiiri iathe kfocwalc^y, aaid was raceeeBftxDy ap^Ued to at least one broadcasting
tfe* c^rc^rt AM i*o4 be^a used extensively in transmitters to date. The
on piat* lo^, power output, and e^casney of a laboratory test on a
CLASS C AMPLIFIERS
7-27
640
180
SO
10OO 2QOO 4QOO
6000 8000 ,1.0000
Etaie Circuit Load Bejstslance
[45
12JOOO 14000
FIG. 35. Performance of RCA 204A as Class C Amplifier
204A is given in Fig. 35. It will be noted that for low load resistances, that is, resistances
that limit peak a-c plate voltages to values appreciably below the d-c supply voltage, the
filter adds little if any to the efficiency of the plate circuit. This is due to the fact that
heavy loads cause essentially one-half sine waves of plate current, so that there are prac-
tically no harmonic components of plate current to reduce.
The results of the experimental data as plotted in Fig. 35 indicate that the efficiency
of a class C amplifier without a filter is essentially constant over practically all the load
range that might be used. The 204A tube, with which the data for the above curves were
taken, was operated at approximately optimum grid excitation so that the values read
from the curves represent approximately the best performance of the tube. Any loss in
the filter for the curves
in Fig. 35 is included as
plate loss, so that the
plate efficiency is actually
greater than shown when
the filter was used.
Oscillograms of the ac-
tual plate current in a low-
frequency class C ampli-
fier were made on an ex-
periment al amplifier ; they o ^ ° "
substantiate the above ex-
planation of the behavior
of the filter and indicate
quite definitely that the
plate current to the tube
at most practical load
resistances is a double
peaked affair, whereas
with the filter the plate
current is essentially one-
half of a sine wave. As a result of the peaked condition of the plate current without
a filter, the peak emission required from the filament of the tube in a class C amplifier
is 6 to 12 times the d-c value; when a filter is used the peak emission required is one-third
to one-fifth of the peak without the filter. The reduced peak plate current requirement
when the filter is used is a decided benefit.
Although the applications of the class C amplifier to radio devices are limited in num-
ber, it is the most efficient type of vacuum-tube amplifier known. When the class C
amplifier is used as the output system for a radiophone transmitter, in which a class B
audio amplifier is used to modulate the plate supply to the class C amplifier, a radiophone
transmitting station is obtained that has a greater overall efficiency than any other type
of transmitter now in general use.
SUMMARY FOR CLASS C AMPLIFIERS. Some of the more important circuit re-
quirements of the class C amplifier as well as some of the more important operating
points are summarized below:
1. If full output is to be obtained from the class C amplifier, the grid excitation should
be sufficient to obtain essentially full permissible d-c grid current at the recommended
bias.
2. The grid excitation for a plate-modulated class C amplifier must be sufficient to
cause a linear relation between the plate voltage and output voltage.
3. In a plate-modulated class C amplifier, it must be remembered that the peak plate
voltage due to modulation peaks is double the plate voltage for normal carrier, which in
turn doubles the average plate current and also the peak current corresponding to a
power four times the carrier power. Therefore, it is necessary to determine whether the
tubes used in such an amplifier are capable of withstanding the peak d-c plate voltage over
an audio cycle and whether the emission of the tube is ample to meet the peak-plate-current
conditions. . .
4. Failure to meet the peak-plate-current condition in item 3, because of emission
limitation or insufficient excitation, results in a second harmonic in the detected carrier
output. Failure to meet the requirements in item 3 only reduces the power output and
efficiency in the case of class C amplifiers for telegraphy.
5. The bias for a class C amplifier must be beyond plate-current cutoff at the highest
instantaneous d-c plate voltage. For 100 per cent modulation the bias should be 2.5 to 3
times the bias for plate current cutoff at normal plate voltage. Excessive bias usually
results in higher excitation power with little gain in efficiency.
7-28 VACUUM-TUBE CIRCUIT ELEMENTS
0. The plate dissipation of a tube in a class C amplifier is determined entirely by the
plat© fupply voltage and the load resistance for normal class C operation of the tube, and
the value 0! load resistance has essentially no relation to the plate resistance of the tube.
7. Tbe ma^tiitiwrn plate efficiency of a class C amplifier is approximately 70 to 75 per
cvnt for all practical load resistances. This efficiency may be raised to SO or 90 per cent
fey wring somewhat higher resistance plate loads if a band-pass filter is used hi series with
the plate,
&. Hie hsoid-pass filter also reduces the peak-plate-current requirements, which tends
to rtdnae dfafeortkm at high percentage modulation.
0. Tfefc audi-o power required to modulate the plate circuit is 50 per cent of the amplifier
input plat* power; therefore, any increase in plate efficiency reduces the modulator power
& REGENERATION AND ITS PREVENTION
COHDITIOH S FOR REGENERATION. In each of the theoretical amplification equa-
tkms feq*. [4], [6], etc.) the internal input impedance Z& appears. When rt-s is a positive
quantity the greatest amplification will be obtained by making the internal input impe-
dance as great as possible. However, it is possible for r,-2 to have a negative value (p. 5-49)
when the external plate impedance of the succeeding tube is inductive. In this casa the
conditions uirader which maximum amplification will be obtained are quite different.
If rs U segmtive and kss than twice the magnitude of the resistance presented to the grid
filament terminals by the rest of the input circuit, it is possible for the amplification to be
fr*a£er than the value obtained when the Internal input impedance is infinite, for the plate
cwnfet of a single tube "m terms of the impressed voltage is (see eq. [1], p. 7-03)
(20)
r?y(?t't jx-^i
n 4- r, 4- ifa -f *,) i. r, -I- 1 \
(20a)
If either r» or £* is infinite, the first factor reduces to tie ft , but if r,- is negative and less than
twice tlie magnitude of re (and x» and x« are of opposite sign and their sum less than x») the
first factor will be greater than jur'f. The tube is then said to be regenerating. In particu-
lar when the denominator is sero the amplification will be infinite and the tube will oscillate;
thai is, plate current of a particular frequency will flow even when there is no externally
iS3apra»d aJtematinu voltage on the grid.
In an impedasMse-capitatance coupled amplifier (eq. [6], p. 7-04) regeneration occurs
Wl»ii tranricnarix^eoapletl amplification is need and the circuit is properly tuned (eq.
P*I> ra«&i*®rm&ls$i wsciira when 0 > rif > 2r^ and oscillation when r& = ~r4.
Hie eetttwrirnt mg@£ift reti^aiicr of the input circuit is caused by the plate voltage
*foetrc*t*tiaa% iodoci»K a voltage between the grid and filament which has a component
with tfe* imiweaeed grid voltage. This will occur only when the plate load is
. (B©e p. 5-49.) A similar voltage impressed on the grid by any other means
of www, haw the same effect. (See Regeneration, Theory and Experiment, by
«m, Kiwr, and Ware, Free. LKJ8., October, 19S5.) Circuits are frequently designed
m thai pert <rf the *mrfy m the plate circuit is "fed back'* to the grid circuit to increase
the tduplifieation. When the feedback is inductive through a movable coil, this coil is
.
1IW1CTS OF UGnVKATIOH. The increased amplification obtained as a result
^ i«»f««mtwi is gc^^etiims® w&d t© iBcreafe gain, partieulaxly where a single frequency is
oetat a«pitei Smae a r«®isiaerativ0 csiraiit usiially behaves like a very sharply tuned
««wit it is not useful when & broad band of frequencies must be amplified.
E^w»r»ii«i tftrtito in a dewaee is th® elective mfsit resistance of the amplifier and
eo tfamwi!® the mm-rt^f^rmtrre wnj^Soitkm obtainable from the tube.
Ai a nil* moet diftwlty b eip^iaaced at radio frcsquencies. Even if regeneration is
pmnrated at the working freqwney c4 tfee amplifier, there may be considerable feedback
^^1?****?: tf * r*WM1*Ilt ^^ e*i^ •* «ae <rf these high frequencies a parasitic
^^wc«»*«w »aj bepn. This may ea&s© the amplifier to cease functioning as an ampli-
Itar. and wro^ p^ectiw ^vi« limits the plat© current the tubes may be over-
heated wy "^
REGENERATION AND ITS PREVENTION
7-29
Another type of parasitic oscillation may exist in the pushpull circuit shown in Fig. 31 ;
in which the input circuit has a certain impedance from ground to grids, because of the
leakage in the center-tapped grid and plate inductances. This condition effectively places
the pushpull tubes in parallel with an input and output circuit with the neutralizing con-
densers ineffective. If the input and output circuits have sufficiently high impedance
(which may be comparatively low for high-power tubes) parasitic oscillations will result.
However, it should be noted that TI and r£ in Fig. 31 are connected from their respective
grids to ground so that the resistors are still effective in suppressing parallel parasitic oscil-
lation of the tubes. If the corresponding value of resistance in r\ and r2 is placed across
the grids without the r-f ground at the center point, parallel parasitic oscillation of the
tubes may exist because the grids would be at essentially the same potential so that the
resistances would be ineffective.
This type of parasitic oscillation is apparently responsible for the self-oscillation of
most pushpull audio amplifiers.
PREVENTION OF OSCILLATION. Regeneration to the point of oscillation may be
prevented in several ways. It is often accomplished by the introduction of power-absorb-
ing resistors into various parts of the amplifier circuit, but these invariably increase the
losses in the circuit and so are objectionable. Another possible method is to decrease
the impedance of the input circuit, but this is frequently impracticable without too great
decrease in amplification.
Parasitic oscillations may sometimes be prevented by so changing either the plate or
grid circuit that the resonant frequencies of the one have no counterpart in the other.
There is then no complete resonant path at any frequency. In general, if the leads to the
grid are short, and a small r-f choke is inserted in series with the plate to increase the effec-
tive length of the plate leads, there will be no common resonant frequency. If the circuits
cannot be so unbalanced resistances must be used, such as are shown in Fig. 31.
The most effective cure for parasitic oscillation of pushpull audio amplifiers is to un-
balance the input and output circuits by placing a resistor or small condenser across one
side of the input or output transformers. In general, the value of impedance required
to suppress the undesired oscillation will not noticeably affect the frequency characteristic
of the amplifier.
Improvement in shielding between stages will sometimes eliminate enough of the feed-
back to make the circuit stable, or the plate and grid circuits may be moved apart if prac-
ticable. Shielding for pentode or tetrode r-f amplifiers is always necessary. Shielding an
audio amplifier is usually not necessary with proper placement of the various tubes and
transformers for minimum feedback. However, it may be necessary to use elaborate
means to prevent stray pick-up to the input transformer. In general, a magnetic shield
for audio frequencies is better than a copper shield, but the copper is better at radio fre-
quencies.
Where the feedback is due to the grid-plate capacitance, this capacitance may be
eliminated by electrostatically shielding the plate from the grid. This has been done in
the tetrode and pentode. It makes possible the extremely high amplification factors
obtainable with these tubes.
NEUTRALIZATION. When it is impossible to eliminate the fed-back voltage it is
still possible to cancel its effect by introducing an equal and opposite voltage. Circuits to
accomplish this are based on the impedance bridge principle or on the three-winding trans-
former. (See p. 6-12.)
The first method for neutralizing the grid-plate capacitance was that of Rice shown in
Fig. 36. Diagram A of this figure is a schematic sketch of connections; diagram B is the
resolution of the circuit into that of the three-winding transformer. From the theory of
Input
rJ£-C^
6 } *• \c
L2
n
^Ci
.11
[llflj
7
U
C2
II
OlK
u
JIQQOOQOOO,
^
,0 Output
!LI
It a
e
L
No Voltage If
Unity Couplinr
:°3
A. Schematic Diagram
B. Equivalent Circuit
FIG. 36. Rice System for Neutralization. The tuning and bypass capacitors shown in the circuit
diagram on the left are omitted from the equivalent three-winding transformer diagram on the right.
7-30
VACUUM-TUBE CIRCUIT ELEMENTS
tlie ttsree-wiiwiiag transformer any voltage induced in the coil a-c will cause no voltage drop
mmzm b-0re (except that due to incidental resistance of the coils) if the value of On is
properly ebcnea and tfac coupling between 6-a and a-e is unity. In practice the con-
denser (C«) is ma4e variable to permit its proper adjustment and is called the neutralizing
coiicleriiaer. The disadvantages of the Rice method lie in the fact that part of the input
voltage acrws ®~« is toot since it is not impressed on the grid, and that neither side of the
nfrutralixin^ condenser can be grounded.
A nwlificatkMi of the Rice method is shown in Fig. 37, A being a schematic diagram
©f epaiiiscikKia. Diagram B shows that this circuit can also be resolved into a three-
wiodiiig traawfornMT circuit. From the theory there will be a value of C«. for which the
iroltagft acn^is 6»« wiH be very k»w, approaching zero as the resistance of c-a-f decreases.
This system is not so useful for power amplifiers as the Rice system; the plate circuit of
ll»® fetter taa be more favorably loaded because the entire plate coil is in the plate circuit.
Schematic Diagram
. Equivalent Circuit
37.
Modified Eke System for Neutralization. The tuning and bypass capacitors shown in
; ctofcKram <m the kit are outfitted from the equivalent three-winding diagram on the right.
Both th«ae nfcfthodi require that for perfect neutralization the coefficient of coupling
be unity and thafe the incidental resistances be sero; hence perfect neutralization can be
only spfsreaeiitfci.
A p^shpnil r-l amplifier can be neutralized, as shown in Fig. 31, by means of the con-
dcnaera C't and C», tlw value of which is equal to the grid-plate capacitance of the tubes
for symmetrical input and output circuits.
In general. slikMiag of the input and output circuits of a capacitance-neutralized
ampJilser a«»©d M>$ be so complete or effective to prevent feedback as for the screen-grid
tube amplifier, foemaae some stray magnetic or capacitance feedback can be effectively
^©d fw fc$r tfae proper adjustment of the neutralising condensers for minimum
A eoTOBEiQia and convenient method to adjust the neutralising capacitance
. i to apply a signal to the grid of the amplifier to be neutralised with the tube in
placw ami the fil&m©i^l*ifet*sd but without plate voltage. An r-f galvanometer is placed
m %b® plat® tank ctrtoit, asd tlie neutralising capacitances are adjusted for zero or mini-
mnm galvaMMBetet deHeetkm. Precaution against exce^ive currents through the gal-
TMwmrtw must be taken for the initial adjustment of the neutralizing condensers, or
other metb&cb of indkatiag & tank voltage may be used.
If the amplifiwr to be i&eutratiwed is a plate-modulated class C amplifier the simplest
and quickest met&od for neutralising is to overmodulate the amplifier and adjust the
neutraiiainK «i»ndeiM^r until the instantaneous value of carrier will be zero at the peaks
of dowinpard modulation. A cathode-ray oscillograph may be used as an indicator for
BIBLIOGRAPHY
timely Small Tubes, Proc. I.R.E., July, 1931.
is Class B and Class C Amplifiers, Proc. I.B.J?., March,
J£ X, Gf*$$itai DetenninAtkm <^ Performanee of Push-poll Audio Amplifiers, Proc. I.R.B.,
A, ?, Ll«chnnf Th« Output Characteristics of Amplifier Tubes, Proc. I.R.B.,
^*Z^^^i ^3^^ £ly ^J^^l referring to the Proc. I.R.E.
«"-«-
WIDE-BAND AMPLIFIERS 7-31
SPECIAL-PURPOSE AMPLIFIERS
By E. L. Clark
A special-purpose amplifier, as the name implies, is a particular type of vacuum-tube
amplifier designed for a definite purpose. Such amplifiers are usually of the capacitance,
impedance-coupled circuit type, as differentiated from tuned and mutually coupled
amplifiers.
A wide-band amplifier is an amplifier that covers a wide frequency spectrum, such as
is used for a television video amplifier. In most cases, the wide-band amplifier operates as
a class A amplifier with plate current flowing for 360 electrical degrees. A wide-band
amplifier is characterized by low gain; for a given tube the gain multiplied by the band
width is a constant.
A cathode follower is an amplifier which has its output load in the cathode circuit of a
vacuum tube. The characteristics of a cathode follower are: reduced input capacitance,
increased input resistance, reduced output impedance, a gain of less than 1, and no voltage
inversion. The cathode follower may be used as an impedance matching device, without
the use of a transformer.
A grounded-grid amplifier is an amplifier that has its grid grounded, and the input
signal applied to the cathode. The output circuit is in the plate, in the usual manner.
The characteristics of a grounded-grid amplifier are: low input impedance, low input-to-
output capacitance due to the shielding action of the grounded grid, and no voltage
inversion.
An in-pnase amplifier is one hi which the polarity of the output signal is the same as
that of the input signal. This is of no importance in sine-wave work. However, for pulse
work and for television video amplifiers, the polarity of the amplified signal is of great
importance.
A negative feedback amplifier is an amplifier in which some of the output signal is
fed back to the input to modify the output. There are two general types of feedback
amplifiers, the voltage-feedback and the current-feedback types. Both are characterized
by a reduction in gain. However, the voltage-feedback type gives an apparent decrease
in plate resistance. Both types of feedback give a reduction in distortion.
A one-shot amplifier is an amplifier which, after responding to an input pulse, will not
respond to a second pulse until a given time has elapsed. This amplifier is similar to a
multivibrator, and it requires two tubes. The characteristic of a one-shot amplifier is
that, after a given input level has been reached, the output is a sudden sharp pulse which
cannot be immediately repeated, a definite time interval being required before a second
pulse can be obtained.
A pulse amplifier is an amplifier that is designed to handle a pulse type of input signal.
Pulse signals are of two general types: positive pulses and negative pulses. The pulse
amplifier must be designed for the polarity of pulse to obtain the optimum performance.
The band width of the pulse amplifier must also be adjusted to the type of pulse being
handled if the pulse shape is not to be degraded and if maximum gain is to be obtained.
The characteristic of a pulse amplifier intended to handle positive pulses requires that
it be biased nearly to cutoff and that it shall approach class B operation and efficiency.
However, to handle negative pulses the vacuum-tube bias must be near zero, and a heavy
plate current is drawn except when the pulse signal is applied. This results in low effi-
ciency for a negative pulse amplifier.
5. WIDE-BAND AMPLIFIERS
The wide-band amplifier is used when the frequency response must be extended beyond
about 15 kc. It finds its chief application as a video amplifier in television equipment.
However, it is finding other uses such as in radar and pulse work. In order better to
understand the frequency response limitations of an r-c coupled amplifier, see Fig. 1.
This is a curve of output voltage vs. frequency, of a typical amplifier stage, as shown in
Fig. 2. The frequencies 5/i and h are considered the useful limits of the wide-band am-
plifier. This is somewhat empirical, but practice has shown it to be desirable in order to
reduce the low-frequency phase shift (see p. 7-46). If many cascaded stages are used
it may be desirable to take 10/i instead of 5/i as the low-frequency limit of the amplifier.
HIGH-FREQUENCY RESPONSE. The high-frequency range will be defined as that
region lying above about 1 kc. The simplest form of wide-band amplifier is that shown
in Fig. 2 with a low value of plate resistor (rz,). In general, pentodes are used for wide-
7-32
VACUUM-TUBE CIRCUIT ELEMENTS
band amplifiers, for two reasons. First, the Miller capacitance effect is negligible; second,
they are made with a, higher mutual conductance (gm) than triodes. The general formulas
for a class A amplifier, eqs. (1), (la», and (2) (p. 7-03), also cover wide-band amplifiers.
However, the value of Z is of interest and governs the gain and band width of the amplifier.
In Fig. 2* Or is the total shunting capacitance, composed of the stray circuit capacitance,
the raitput capacitance of Fj, and the input capacitance of V$ (which may be partly
Miller capacitance in triodes). Let the resistance r0 represent the resulting
100
I
|70.7
/. A
FIG. I. Ampli&er Resixmse Curve
Cs
Hh
1!
-*-+
-JL-
* +B -C
Fio. 2. Uz^mipaosated Amplifier Stage
pwalk! r«i^iuaee of tfe* |^lat€ reebtor TL ai^i the grkJ resistor rx. The absolute value of
Z a given by
A* th» ^r^^»^ j^ wU^ imakes t}^ ©aimcitance reactance ** e<jual to r0, the response
inn be ckmn to 7^.7 per «»t i^ the maximum response. This gives a means of determin-
ing $h® valu* el f r-
A* tk9 plM« r««^or ri in «»m% m«di smalfer thaa rr? the effect of rg is usually negligible
IMC !«. »*»• aratoal oomtectance of Ube vacuum tube, the gain of the stage is
Gam A =
n becomes
in .4 - gmZ
«reil*Br
stage is
(3)
', therefore
(4)
(5)
WIDE-BAND AMPLIFIERS
7-33
for parallel resistance and capacitance as shown in Fig. 2 which represents a time delay of
0.035
j
• seconds
(6)
For an un compensated amplifier: Fig. 3 gives the value of TL for various values of shunt
capacitance CT, at the frequency /2. The response will be down to 70.7 per cent of the
fiat portion of the curve at frequency /« when using a plate load TL as determined from Fig. 3.
10,000.
100.
1,0
Frequency /2, megacycles
10.0
FIG. 3. Plate Load (TL} in Terms of Frequency (/2> and Total Capacitance ((7jO for an Uncempen-
sated or Shunt Peaked Amplifier
SHUNT PEAKTTTG. In Fig. 4 is shown the schematic of an amplifier stage using
shunt peaking. As previously described, Ct is the total shunting capacitance. The gain
for this amplifier is given by eq. (4) . The value of Z is
(7)
+B -C
FIG. 4. Circuit for a Shunt Peaked Amplifier Stage
If an inductance LI is chosen so that XLI = J/2 %CT at /2, the resulting impedance Z will be
equal to rz,. This means that the response will be flat to frequency /2 instead of being
7-34
VACUUM-TUBE CIRCUIT ELEMENTS
40C
1000 2000 3000 4000
Plate load rL, ohms
5000 6000
5, Shunt
in Terras of Frequency f/j) and Plate Load (TL) for a Shunt Peaked
Amplifier
10,000.
. X ,. i !x X
X iX i X \ x
X X X i X X
X \i i \| ! |.\ \! \
\ i \ I
X l\
\gj
^xi
x<?
\
^ 2a-/2CT"
s
&L
\
\
\
\
\
\
1.0
g, megacycles
\
\
\
\
\
\
\
\
\
10.0
(Cr) for a Shunt Peaked
WIDE-BAND AMPLIFIERS
7-35
down to 70.7 per cent as in the uncompensated amplifier. The values are
1
(8)
T L
Li = -—
43T/2
(9)
(10)
Gain A = gmrL
The time delay is no greater than 0.023//2 seconds.
Figure 5 gives the value of inductance LI, for various frequencies fa and load resistance
TL for use in a shunt peaked amplifier.
A shunt peaked amplifier can be designed quickly by the use of Fig. 3 and Fig. 5. Know-
ing what frequency /2 is needed (say 3.0 megacycles), determine the value of Ct\
400
1000
2000 3000 4000
Plate load rt, ohms
5000
6000
FIG. 7. Shunt Inductance (Li) in Terms of Frequency (/2) and Plate Load Resistance (TX) for a Shunt
Peaked Amplifier with Corrected Phase and Amplitude Characteristics
a good estimate. Then from Fig. 3 find TL to be 1330 ohms. Now from Fig. 5 at 3 mega-
cycles and 1330 ohms, LI is found to be 35.2 microhenrys. The stage gain will be 1330
times the mutual conductance gm of the tube in mhos.
For multistage wide-band amplifiers where the best phase and amplitude character-
istics are needed, slight revisions in eqs. (8) and (9), as shown by Freeman and Schantz,
will give almost perfect results up to frequency /$
TL =
0.85
0.353ri,
(ID
(12)
Equations (11) and (12) are plotted in Fig. 6 and Fig. 7 to facilitate the design of such an
amplifier.
SERIES PEAKING. Figure 8 is the schematic diagram of a series peaked amplifier.
It can be seen from Fig. 8 that the capacitance is split by the inductance L±. This results
in the vacuum tube Vi working into a smaller capacitance than in the previous case of
shunt peaking, with the results that more gain is obtained. For proper operation the
ratio of Ci/Cg = x/2. If Ci/Cg — 2 the plate load resistor TL must be put on the other side
of the series inductance La. The rule is to keep the plate load resistance TL on the low-
7-36
VACUUM-TUBE CIRCUIT ELEMENTS
L2 CG
VV
-I-
^-4-
+8
Fm. ft. Circuit for a Series Peaked Amplifier wh
ssck? 01 th*? series inductance £3. The value of TL for series peaking is given by
(13)
TL
TL
__
4rCi/s
'fjert < V Cj "•*/!. In i&oet ca^es* however, it is more convenient to use CT, the sum of
> f "j, an<J atrmya, onee C'r ma be determined more accurately than Ci- In terms of Cr,
j. m ci^^a fey
^
If the »»ri@§ iWbctj^©© Z« is c&oaen to resonate with d at a frequency of /s^a, the
witt be $a& lo f rwineiicy /s. Tb© yalne of the ser^ inductance L* is given by
% m tenm of C
SiibsiJtwUFtiMc £
10,000,
y, £3 » ©
i® vatlue !
STCrr
rfCV
froi
n e
L®
q,
2
d
^5
s
4
U
)
-^
r
li
ra^>
rafti
^L
V.xt/^
(16)
— - -\r— —
1 \^
S^
j-
k — Nc
, x
T -
1
5
\
\
S^
i
X
s
L
2
1C
f?
CT.
x
\
\
X
X
\
o'
X
\
t
\
1
\
^
\i
N
\ o
S^s
\
\
IN
N "
Xy ^
X
vJ
%
\
\
\
\
\ ,
N^
^t
%J
N
\
\
\
^
\
^
S
X
\\
1
N
S
\
X,
>
s
1
*• 1OOQ
\
\
\
C
S
s
3
^
Xj^
\
*«•
\
\
\
\
s
S
V
•v
•\rv»
x^
Sj
x.
^
i
^
x
^
jtg
>
^ *
\
^
X
NS^
\
"5
,
\
\
O.
<
\
\
x^
S
X
^
\
\
[\
s
\
\
s
X
N
\
\
\
100.
\
N
\
\
\
\
\
s
V
ta TMM of
10.0
f^t megacycles
•ad Total Capacitanee (Cf) for a Series Peaked
WIDE-BAND AMPLIFIERS
7-37
The phase delay is a rather complicated function in the series peaking circuit, but in
general, as Seeley and Kim ball have shown, the time delay up to the frequency ft is con-
stant within a variation of 0.0113//2 seconds. This is roughly one-half the variation in
800
1000
2000 3000 4000
Plate load rt, ohms
5000
6000
FIG. 10. Series Inductance (L2> in Terms of Frequency (/2> and Plate Load (TX) for a Series Peaked
Amplifier Stage
phase delay experienced with shunt peaking. The gain of a series peaked amplifier is
given by eq. (10), using the value of TL as obtained from eq. (14).
To facilitate the design of a series peaked amplifier eq. (14) is plotted in Fig. 9 and eq.
(16) is plotted in Fig. 10. The curves of Fig. 9 and 10 are to be used as described in shunt
peaking.
COMBINATION OF SHUNT AND SERIES PEAKING. As might be expected, the
advantages of shunt and series peaking can be combined to increase the gain further.
-C + +B -C +
FIG. 11. Circuit for a Combined Shunt and Series Peaked Amplifier Stage
The series inductance La separates the output capacitance Ci and the input capacitance
Cs, while the shunt inductance LI compensates for the output capacitance Ci. The cir-
cuit is shown in Fig. 11.
?~38 VACTUM-TUBB CIRCUIT ELEMENTS
10,000,
rx
I
<g 1000.
-2
at
£
s:
X TV
^!~T
N
\
X
N
\
^-VJ
^U
\
>j i
j\
01
ffl
"~^\
X
^
SJ
\
N
IX
\
\
\
\
\
\
1.0
Frequency fzf megacycles
10.0
F»«, 12. H»*e L©«d CrU ia Tetms ol Freqweacy (/2) and Total Capacitance (Cr) for a Combined
Shunt-serres Peaked Amplifier Stage
2000 3000 4000
Plate load rt,ohms
5000 6000
WIDE-BAND AMPLIFIERS
7-39
Again, as in series peaking, the ratio of Ci/C2 = */2 for proper operation.
1.8
LI = 0.12CFTZ,2
If the value of CT from eq. (17) is substituted in eq. (18) and (19), they become
0.936rL
(17)
(IS)
(19)
(20)
(21)
The gain of a combined peaked amplifier is given by eq. (10) using the value of TL as
obtained from eq. (17).
800
5000
6000
°0 1000 2000 3000 4000
Plate Load ru ohms
FIG. 14. Series Inductance (£2) in Terms of Frequency (f%) and Plate Load Resistance (TL) for a
Combined Shunt-series Peaked Amplifier Stage
The phase-delay expression becomes more complicated in this type of peaking, but it
does not exceed 0.015//2 seconds, up to /2.
If the Q of Z/2 is too high, a high-frequency peak will be experienced just before f% is
reached. The resistance r2 shunting LZ is to lower the Q of the inductance £2 and prevent
the formation of a peak in the response curve. The value of resistance r^ may vary from
5 to 10 times the load resistance TL.
Equations (17), (20), and (21) are plotted in curves, Figs. 12, 13, and 14, to expedite
the design of a combined shunt-series peaked amplifier.
CONSTANTS-TYPE FILTER COUPLING NETWORK. The schematic diagram,
Fig. 15, shows a wide-band amplifier of the constant-jK, low-pass filter type. This circuit
appears at first glance like the combined shunt-series peaking network; however, its con-
stants are based on standard constant- JT low-pass filter equations, as follows: L% = —
and Cz = In forms to apply to the circuit of Fig. 15 these become:
TL = -£gr (22)
Lz = ri?Cz - ^- (23)
la - ^ (24)
7-40
VACCUM-TOBE CIRCUIT ELEMENTS
»n<I r2 - 5 to 10 tin* n. The stage gain is still given by eq. (10) iiang the valu of r^
fr,«n «*i. «±J, Thi- Indicate higher gam than any of the other high peaking systems.
Th» li true; however, one factor ha. been ignored in all the foregoing systems, namely
capmciunce. Only the distributed capacitance CA across the series coil as
Fro 13. Circuit fc*r a Wide-hand Amplifier with a Constant-JT Configuration Low-pass Filter-coupling
Network
thown IB Fig, 15 h*a mueh effect. This capacitance, however, changes the seeming con-
*t*nt-K tow-paw filter coupling network into an 3£-derived filter section. In most wide-
bs«d ampliSers tb» frequencies encountered are high enough so that this effect cannot be
ignored. In changing from a constant-lT to an M -derived low-pass filter, there are two
ways to k«*p a giwn pass band: to reduce the shunting capacitance, or to reduce the
irapedimee. As the capacitance cannot be reduced, the only course is to
tbe load resistance ri, thus lowering the gain. The equations, taking this dis-
I capacitaacse €4 into consideration, are as follows:
'$ (25)
(26)
(27)
fJS
Also Lj «» O.SZ-2 approximately, and r» — 5 to 10 times TL-
Equmtioa (28) giv&s the frequcnc>* of infinite attenuation which sliould be kept well
outaid* tli@ pa^s imad to preveat excessive phase shift.
M
/*
(28)
Cnder laorm&l c*>aditioiis the phase shift is about the same as for the combined shunt
ttd series peaking ^nst«ni.
Eqaatk>a (25) is plotted ia Fig. 16, which gives the values of M in terms of the output
1.2 r
1JJ
O.s
9,4
as
RfltlO CEf •
Fs*. ML V*tat si Mm Frodwed bw
a»d the
0.5
C&p«^taiacc Wd) ol tiie Series Peaking Coil (
»ri (Rg. 15) — ^ %>«" \
WIDE-BAND AMPLIFIERS
7-41
capacitance Ci and the distributed capacitance C<t of the series inductance L«. The curve
in Fig. 17 shows the effect of JJ on the load resistance TL and the series inductance L$. As
the stage gain is directly proportional to the load resistance TL, the importance of keeping
the distributed capacitance Cd as low as possible is apparent.
120
3-0 0.9 0.8 0.7 0.6 0.5 Q.4
Value of M
FIG. 17. The Effect of M on the Plate Load (TL) and the Series Peaking Inductance I
Equations (22), (23), and (24) are plotted in the form of curves in Figs. 18 and 19 to be
used for designing wide-band amplifiers of the constant-.?? configuration. Knowing the
top frequency ft (say 3 megacycles), determine the value of C*; 25 /*/if is a good estimate.
Then from Fig. 18 find TL to be 4240 ohms. Now from Fig. 19 at 3 megacycles and 4240
ohms find L$ = 448 microhenrys, and LI = 224. However, the distributed capacitance
of Z/2 must be considered. It may be about 4 /z^f while Ci may be approximately 16 jujuf.
10,000.
100.
0.1
1.0
Frequency /2, megacycles
10.0
FIG. 18. Plate Load Resistance (rz,) in Terms of Frequency (/a) and Input Capacitance (Ca) for a
Constant-.^ Type Low-pass Coupling Network
This gives a ratio for Cd/Ci of 0.25; referring to curve Fig. 16 M is found to be 0.78. Re-
ferring to -Fig. 17 at the point M = 0.78 the value of TL will be 78 per cent of that for a
constant-K network and the value of L$ will be 60.8 per cent of that for a constant-J^
network. These factors modify the value obtained above, TL becomes 3300 ohms, and £.3
7-42
VACUUM-TUBE CIRCUIT ELEMENTS
900
0
F&s, if
IQOQ
5000
6000
2QQQ 3GCQ 4000
Bate load rv,ohms
InduetMMM (!i) Bad (La) in Terms of Hate Load Resistance (rx) and
> fur a Constant-^ Type Low-pass Filter-coupling Network
.„- ,_i 272 izucrohe&ryB. From the above derivation Li = 218 microhenrys, which is
appnmmattly that obtarod from Fig. 19. The shunting resistor r, would have a value
•onMrfcm fattwwn 15,000 cfens and 33,000 ohms, depending upon "the Q of the peaking
Its exact TmJiie would have to be determined by test.
Type #f r»d«a Swwu SifMl Used to li*t
L
_r
»-ft-o.
c-£»u
1.0 je
Loading Resistor r2 Too Large
Fio. ^. Curve Shape Obtained When the
Loading Resistor (r2) Is Too Large
5 i
With
Type)
Fw.
loading R?sZstoi-r2Too Small
. Shape Obtained When the
Loading Resistor (rj) Is Too Small
Plate Resistor rLToo Large
No FIG, 24 Curre Shape Obtaiued When the
Plate Load Rector (J-L) Is Too Large
WIDE-BAND AMPLIFIERS
7-43
observed across a very low plate resistance, possibly 100 ohms. Figure 20 shows the
response of the wide-band amplifier of the constant-^ configuration when all its com-
ponents are adjusted properly. Figures 21 to 28 inclusive give the response obtained
with various components that have incorrect values.
Plate Resistor rL Too Small
FIG. 25. Curve Shape Obtained When the
Plate Load Resistor (rx) Is Too Small
Js JmitT
Series Psakfng CoFI L2 Too Small
FIG. 27. Curve Shape Obtained When the
Series Peaking Coil (£5) Is Too Small
J V
Series Peaking Coil L2 Too Urge
FIG. 26. Curve Shape Obtained When the
Series Peaking Coil (La) Is Too Large
Shunt Peaking Coil Lj Incorrect,
Too Large or Too Small About The Same,
FIG. 28. Curve Shape Obtained When the
Shunt Peaking Coil (Li) Is Incorrect
Multistage wide-band amplifiers using pentodes or beam power tubes offer no particular
difficulty. However, if a multistage triode amplifier is to be designed, trouble will be en-
countered if peaking is used in the grid circuit and plate circuit of the same tube, as it
may result in a tuned-grid, tuned-plate oscillator.
FIGURE OF MERIT FOR WIDE-BAND AMPLIFIER TUBES. The capability of a
vacuum tube to amplify at high frequencies depends not only upon its mutual conduct-
ance but also upon its input and output capacitances. It is these capacitances, in addi-
tion to the stray capacitance, that limits the value of plate resistance TL that can be used.
The "Miller" capacitance effect is the chief reason triodes are not satisfactory as wide-
band amplifiers.
Considering these factors, eq. (29) gives an acceptable figure of merit (F.M.) for wide-
band amplifiers.
F.M. =
gm
Csk
pk -f Cgp(l + JL)
(29)
Equation (29) is applicable to either triodes or pentodes; for pentodes and beam power
tubes Cgp is so small that the last term may be ignored, hence:
F.M. = •
(30)
-f Cant
Table 1 gives a list of vacuum tubes with their corresponding figure of merit.
Table 1. List of Vacuum Tubes Applicable to Wide-band Amplifier Service, and Their
Figure of Merit
Tube Type
Input
Capacitance,
Output
Capacitance,
Gm
F.M.
6AK5
6AG5
4.0
6.5
2.8
1.8
5,100
5,000
750
602
6AC7/I852
11.0
5.0
9,000
562
6AG7
13.0
7.5
11,000
536
6AU6
5.5
5.0
5,200
495
6BA6
5.5
5.0
4,400
419
6AB7/1853
8.0
5.0
5,000
385
6SH7
8.5
7.0
4,900
316
6SG7
8.5
7.0
4,700
303
6L6
10. 0
12.0
6,000
273
6V6GT
9.5
7.5
4,100
241
954
3.4
3.0
1,400
219
6K6GT
5.5
6.0
2,300
200
COMPARISON OF HIGH-FREQUENCY COMPENSATION METHODS. Table 2
gives the essential design data for high-frequency compensation of wide-band amplifiers.
The last three types listed as "practical results" give data obtained by measuring the
7-44
VACUUM-TUBE CIRCUIT ELEMENTS
con*tam-£ network response, with different ratios of d/C2. As the distributed capaci-
tance <• d winnot be eliminated, it must be considered as producing an ^/-derived low-pass
filler network.
Table 3. Summary of Wide-band Amplifier Formulas
Type
Relative
Ll Gain at /2
M
"C wsora p«? i »&t ®d
0.707
1. 00
Sfaunt f^*f bwt
0,85
j 0.85
Ci 'Ci * 0.5 ,.
1.5
1.5
1,8 i 0.52CJTL1 O.I2Crris 1-8
Zr/jCr
3.0
C@«pl&!it K *nth i
Ci/Ci * S.5
3.0M
Practical Results
0. 8Z,2 a pp.
Crf
OMMKUAI K wnfe C<
O.&Liapp.
2.55Jf
t A' »ith
Ci/< j » 1.0
O.SLs app.
^
Gain «• rx,Gjtf
LOW-FEE QtJEHCT RESPGJTSB, Low-frequency atteauation or low-frequency am-
aad plyise ahift may be introduced in any one of four places, or a com-
tbt low. Ttey sare (1 > oilhode re^stor and by-pass condenser; (2) grid con-
tor c^jplmg ae^^trk; (3) sateen aai^ly re^stor and by-pass; (4) the internal
- B pow^r supply.
EPFBCT OF A CA.THOBK RESISTOR A2TD BY-PASS. One method of obtaining
a aeigftUY* bm& oa tW grid of a vacuum-tube amplifier is to include a resistor rk in series
with tJb* o^toie l» ground; to preheat low of gain, this resistor r* is shunted by a capaci-
tor (V S» Fig- 39. Th« effect of this Has network rjtC* on the low-frequency response
by tins ffcet tl**&, the feynrer tlie freqi^aey, the higher the capacitive reactance of
the k«i ita fllraatniff effect oa r4. This results in cathode degeneration with an
loss iri (UA. Tb« gain of aneh an amplifier stage is given by:
wad the
Gain A »
(31)
k given by
C51 *
ger.eral fornraia. For a wide-band amplifier the tube is usually of the
«>:» O. »»^ ^ » 1.0, so TLJT* aad !/*> may be disregarded,
<»
WIDE-BAND AMPLIFIEKS
7-45
To prevent loss of gain at the lowest frequency, Zk must remain essentially constant. In
practice this may mean hundreds of microfarads for Ct, especially if r* is low. It is pos-
sible to compensate for the loss of gain due to cathode degeneration by a plate filter
in the plate circuit of the amplifier stage (Fig. 29). The conditions that must be
+B
FIG. 29. Amplifier Stage Considering Low-frequency Response Only
met to compensate for the TkCk network are: rtCj- = rpCp, rp/rt = rigm, and
rLgm, from which the values of TF and Cp are obtained
and
(34)
(35)
THE EFFECT OF THE GRID COUPLING CAPACITOR-RESISTOR. With a grid
coupling condenser CG and resistor rg, Fig. 29, the voltage 63 impressed on the grid of Fa
will decrease, as the frequency decreases, assuming e* to remain constant. The ratio
€3/62 is given by
At the frequency that makes the capacitive reactance 1/wCe equal to the grid resistance
r<y, the response 63/^2 will be 70.7 per cent of that at mid-range frequency, and the phase
shift will be
tan-i if? = 45 deg (37)
TG
The grid resistor TO should be made as large as possible; its value, however, is limited by
the tube manufacturer to a maximum for a given tube type. For a given low-frequency
response the value of Co may have to be so large that there is danger of ruining the high-
frequency response by increased stray capacitance to ground. In practice the value of
CG would be 0.05 to 0.10 juf, and r<? would be the manufacturer's maximum value for the
tube type being used. If these values do not give a response at the lowest frequency of
5/i as indicated on Fig. 1T compensation is needed,
Equations (36) and (37) are plotted in the form of curves in Fig. 30. This gives an
easy means of determining low-frequency response before compensation. The plate filter
CFTF, Fig. 29, can be so proportioned that the voltage rise across TI£F as the frequency
decreases can just compensate for the voltage loss across C<?, thus producing fiat response.
Also the phase angles are such as to compensate. To achieve this compensation the time
constants of the plate-filter circuit and grid circuit must be equal, that is, r<?C<? = rx,CV,
from which
CF = ^ (38)
and
(39)
where / is the lowest frequency to be compensated to full response. These equations are
based on the fact that the pentode amplifier is a constant current device within the range
of operation. The value of rp should not be made so high that the amplifier plate voltage
7-46 VACUUM-TUBE CIRCUIT ELEMENTS
fatt» ai^pitwiablF bekw its screen voltage, or trouble may result from too high a screen
4iuftiip*tion.
UtUA% n is preferable to make the cathode circuit such that no compensation is needed
at UM kiwwi frequency required* Then compensate the grid coupling network in the
pl»i« circuit by m**am of the plate filter. It must be remembered that the plate filter
coropeoMttion will tata care of only the loss of lows at one point. Do not try to compensate
for f if* faHPtt by € **£*£& <s»m^«^i<m; it cannot be done.
Phase Angle, degrees
10 100 ' 1000
Frequency, cycles per Second
Fi» 30, Ci*nre, Giiing tbt Low-freqwaey Respoiase Obtained, and the Low-frequency Phase Shift,
wifcb Different (roCG) Grid Coupling Network
TH1 EFFECT OF THE SCREEN BY-PASS. The effect of n£z (Fig. 29) is similar
to that whidi requite from cathode degeneration mentioned previously. However, the
ttreea nirrfsfit is only about 10 per cent of the plate current, and the screen-plate mutual
MMMluetA&c* m only aboiat 12 per cent of tlie control grid or cathode-to-plate mutual con-
d^rtan w. and m the effect is much smaller.
H tb» tniM» aai^mBt €^ r^a ii mad® at legist 4 times as long as the period of the lowest
fraqtMmcy it is dteaned 4a pa«s, tfee efect will be negligible. The value of r2 is determined
by UM nokac* rtfQttirw&eiats fe^* th« particiilar tube being used; then the value of C2 is
lbj:
Cs=5^ (40)
THE EFFECT OF tlttE IWTIRHJLL IMPED AlfCE OF THE POWER SUPPLY. The
supply iBt«armal ittp«diUM« Zi b e^eatially t^ reactance of the output filter con-
. Tfcit r«M9iMM9 bws>tin«^ common for all ampHner stages and may result in the
ol bw«4r«»epi©ttey nwponM or in k>w-lre<|i*ency motor-boating, depending upon the
if $&»gt8, tht rt«pM^, mud the gam of the system.
It h^ been f<atsd that tfee empaciuve remetaac« ore of the final filter condenser in the
twm MHPply «>^*®m, »t tb« bwwt frequency- encountered, should be no greater than 10 per
_„ of tiw ^««4iw fmi load r«sstan» to prei-ent (^mrnon coupling through the B supply.
Tl&t vmtiift ^ tfe« fiaal filter capacitance is then given by:
~-
2w/r
r t« th* *fft4*i<*t k«d mwUnee which is given by:
B c«rr«at of the B supply.
(41)
(42)
CATHODE FOLLOWERS
7-47
In general, when designed for low-frequency response, the cathode circuit is by-passed
with a capacitor of sufficient size to prevent cathode degeneration at the lowest frequency
encountered, or the cathode is grounded and negative bias is supplied to the grid. The
screen circuit is adequately by-passed so that no loss of lows results, and the B supply
impedance is made sufficiently low to prevent trouble. This leaves only the effect of the
grid capacitor-resistor network which must be compensated. This compensation is done
in the plate circuit of tube Vi driving the grid of "Fa, as previously explained.
6. CATHODE FOLLOWERS
The name "cathode follower" is given to an amplifier stage when the load, or the major
portion of the load, is in the cathode circuit instead of in the plate circuit. Figure 31 shows
such an amplifier stage.
This type of operation is called a cathode follower because the cathode tends to follow
the grid in voltage as signal is applied, thus reducing the actual grid to cathode voltage
Piste
Output
Cathode
Output
PIG. 31. Cathode-follower Stage General Case,
•with Resistance in Both the Plate and the
Cathode Circuits
Output
FIG. 32. Cathode-follower Arranged
for Proper Bias by Returning the Grid
Resistor to a Tap on the Cathode
Resistor
below that of the applied signal. This type of circuit finds its widest use as an impedance-
changing device. It is used extensively in connection with wide-band amplifiers to match
a line where a transformer would be impractical.
Cathode followers usually use triodes, since high gain cannot be realized and since the
shunt capacitance of a pentode is high, including screen-to-plate and screen by-pass
capacitance as well as the usual cathode capacitance.
Cathode followers have many characteristics not found in amplifiers of other types:
(1) output from the cathode circuit, (2) voltage gain to the cathode of less than 1, (3) re-
duction of input capacitance, (4) increase in input resistance, (5) low output impedance,
(6) increase in effective plate impedance, (7) no change in polarity of output signal, and
(8) use as a phase splitter with load in both cathode and plate.
When a tube is operated as a cathode follower, the circuit should be so arranged as to
supply the proper negative bias for the type of tube being used. If the circuit is as shown
in Fig. 31, the IT drop across the cathode resistor Tk should be such as to provide the proper
bias for class A operation. When a high value of cathode resistor is needed, the arrange-
ment shown in Fig. 32 should be used. The IT drop across the resistor TI should provide
the proper negative bias for class A operation. If the cathode resistor is so low in value
that sufficient negative bias is not developed, an external negative voltage must be sup-
plied to the grid to produce proper class A operation.
In the general case (Fig. 31) the gain to the cathode is always less than 1 and is:
Gain A =
If the plate resistor is zero (Fig. 32), eq. (43) becomes
Gain A
(43)
§H_± (44)
1 + rrfU/rj,) + gm]
When the cathode load is not a pure resistance, r* is replaced by Z*, which is the absolute
value of impedance at the frequency of interest.
7*48 VACUUM-TUBE CIRCUIT ELEMENTS
For pentock operfttxm i> y> r& » 1, and so the gain to the cathode becomes
Gain A - , f"r* (45)
1 4- rfcgw
The effecthre input cmpadtaac© of a cathode follower is given by
cf,
When the plate resistor ii aero,, eq. (46) becom.es:
C- - C* (' - l+nK!£)+,J + C" (47)
The effective input resistance is given by:
r«H - - ^ - (48)
- __ m _
1 4- (ri/Tf) + rjfc[(l/rp) 4- &*]
Tfcf effeniT^ ofitptit impedance r§ of a cathode follower, for the general case, is given by:
-1
(49)
(49) ia for the t^be alone and do&s not include the effect of the cathode resistor
is in afaunt with rt, Tlie resulting impedance -Zii is given by:
the plate nwador n is aero, eq. (49) becomes:
1
(50)
(51)
In a pentode r» » I, and so r§ « 1 'gw.
In some fa*ea it may be moc« desirable to have Zi the effective output impedance of a
fftthodf follower ia a wngle equation rather than first to calculate rfl and then JZi. The
general ernwe for Zi directly is
Z «sr rl. 4" Tp
3 * 1 4- r^» 4- (1/r*)] 4- (rx/rjb} (52)
Wheis TI fa awto, e*Q. {521 b©c©i»^:
y 1
*« ** /•. j_ . . ., > >. , (53)
to couple into a line, matching its char-
tfeis ^m be done with a matching output
a . , ... -apliSer wf»-k sadi a transformer is not readily available
A vtttnnae faii@iwer i^s fe^ Q^^ i^. g^^j service.
^ "^*.?%e?^* ^r1*11" ^ °< ^« Hoe to be matched is less than r0 for the
th«j ^TMterMe i»p«d«ioe Z of tfee line is hi^ber than the
* ±^*^ "*** " "^ (Re- M)- *" vai»e ^^ tbe
(~ \ { gmfa+Z) \
\r, 4- 2/ \1 4- (r, -f Z)^ 4- (l/r,)]/ (55>
GROUNDED-GEID AMPLIFIER
7-49
the tube plate current; otherwise the cathode follower will not operate. If Tk is too high,
however, the operation may be improved by terminating the line of Fig. 33 for direct
current as well as for alternating current.
When an amplifier operates with an unbypassed cathode resistor (a type of cathode
follower) , the effective plate resistance rp is increased.
rp' - rP(l -f gmrk) (56)
When a cathode follower is operated with a resistor in the plate circuit equal to the
resistor in the cathode circuit, it is termed a "phase splitter." That is, the voltage de-
veloped in the plate circuit will be equal to the voltage developed in the cathode circuit.
FIG. 33. Cathode-follower Circuit Used
to Match a Transmission Line, When
the Characteristic Impedance (Z) of the
Line Is Lower Than the Cathode Imped-
ance (ro) of the Tube (Vi)
FIG. 34. Cathode-follower Circuit Used to Match
a Transmission Line, When the Characteristic
Impedance (Z) of the Line Is Higher than the
Cathode Impedance (ro) of the Tube (Yi)
However, the polarity of the voltage in the plate circuit will be the inverse of the voltage
in the cathode circuit. This type of circuit may be used to obtain pushpull operation
from a single amplifier. The gain to the plate will be given by eq. (31), and the gain to
the cathode will be given by eq. (43).
7. GROTJNDED-GRTD AMPLIFIER
A grounded-grid amplifier is usually a triode which has its grid grounded and the input
connected to the cathode. The output circuit is in the plate in the usual manner. Fig-
ure 35 shows such a circuit. A triode connected in this manner has some of the character-
istics of a screen-grid tube, as the grid acts as a shield between the input and output cir-
cuits. It also has some of the characteristics of a cathode follower, as the cathode-input
impedance is equivalent to that of a cathode follower with a plate load. Another feature
of the cathode-input amplifier is that there is no
voltage inversion between the input signal and yt ^L 1 Output
the output signal as with conventional grid input. '
The input impedance Z\ is given by: t
i ==
1 + rp[gm + (1/rjb)! +
The input impedance Zi of a cathode-input
amplifier may be adjusted to match a line the
same as a cathode follower. Solving eq. (52) for
n gives
J/2 [1 + (TL/rP)} - [gm + (l/r,)3
(57) •=-
FIG.
•f-B
35.
Circuit of the Grounded-grid
Amplifier
The effective impedance Zk in the cathode cir-
cuit must be determined before it is possible to obtain the gain to the plate and the
effective plate resistance rpf. Referring to Fig. 35, r» represents the internal impedance
of the signal input source, and rt is the cathode resistor.
4-
(58)
Where a transmission line is being matched, rj would be replaced by Z, the character-
istic impedance of the line.
7-50 VACUUM-TUBE CIRCUIT ELEMENTS
The fun of the cathode-input amplifier is given by e*. (3D using Z* as obtained from
Gain A ~ ^-~ = ' <31>
It <an be SWB from eq. (31) that to obtain high gain with a cathode-input amplifier the
aubode impedance Z* should be kept low and TL should be made as high as possible.
Making ft high «bo increases the input impedance as shown by eq. (52).
Tin* effectiw plmte impedance r/ of a cathode-input amplifier is given by eq. (56),
•ubetttutiac ZA as obtained from eq. (58)
r/ - rp(l + j?raZ4) (56a)
wtiieh giv*s as increase in plate resistance over that of the tube operated in the conven-
tUMml manner*
a m-PHASE AMPLIFIERS
The name in-phaae amplifier applies to an amplifier that has the same polarity of signal
in the output aa thai applied to the input. In sine-wave operation this is of little impor-
tanr«< but for puisw amplifiers, or television amplifiers, the polarity of the signal is impor-
tant. Ttese types of signals are not symmetrical about an a-c axis and must be treated
Thm are four ®&H;eml typee of in-phase amplifiers:
1. Catted® follower.
2. Oth<xi*-input ampliEer.
3. Combined cathode follower, cathode-input amplifier (cathode-coupled amplifier).
4. Suppressor input, screen output amplifier.
Tb© cathode follower and cathode-input-type amplifiers have been covered in the
lMV**dutg aertkNMi and will not be discussed further,
The third typt of in-pim»e amplifier is a combination of cathode follower and cathode-
iiipiit am plifer, termed cathode-coupled amplifier. This type of amplifier is best made
by nan* a dual trk*$e with a common cathode, such as a 6J6 or a 6SN7 tube. The circuit
is shown in Fig. 36. In an ampli-
-** fier of this *ype the polarity of
utpu the signal is unchanged at any
point through the stage.
The value of rt should be such
that the negative bias developed
by the combined plate currents
of FI and FS is proper for class A
operation of the tubes FI and Fa.
In operation the cathode-coupled
amplifier exhibits characteristics
F***» m. Th» Ia-pfe»w Ampiiiw of tbe Catbode-coupied Type *& some respects similar to those
of a screen-grid tube. It can be
*»cl wkli tuiied input &ad tuued outjmt circuita without danger of oscillation, such as
would omir if a trk*de in conventional circuits were used.
Tlfee gam ®£ (V\) the cathode follower can be calculated by using eq. (31), the value of
Zi obtaffied from ©q. (52 j being mibstituted for Z*. These two equations can be com-
bai»d to give the gam to the cathode of FI; assuming that both tubes are the same, then
Gain to cathode of FI = gm^L + r^ (59)
The c&thode feHower is workiag into the cathode of the second tube which exhibits a
tow ca&!»de4npm impcdbuce, as does any cathode-input amplifier. This cathode im-
ptdaiw must be comstt&mi in the gain equation. This is done by using Z± of the cathode-
istSWf tube aa th» rathodae lo&d for tb.« psi.tKfvl» fnHmcaT- Tk^ ;0 « Tn*^.A. ^-^T..- J.T J.-L..J.
. ± -
liabe M the cmtboae toad for tfee catliocte follower. This is a lower value than that
.
Im obtammjc the gum of the cathode-input section F2, the cathode-output impedance
for the catliodt follower Vj must be used for the cathode load of the cathode-input
nplit^r F^ TEe Talw of Zi from eq. (53) must be substituted for Zt in eq. (31). Com-
Ifa^we two equati0im, the gman of the cathode input section is given by:
Oafa fawn «^b©a« to p48*e of V, - - j^l -|- (ry/r^) + rrfm]
2(1 -f r^w) + (?L + rp)/rk + rm
NEGATIVE-FEEDBACK AMPLIFIEES 7-51
The overall gain of the cathode-coupled amplifier is given by the product of the gain to
the cathode of Vi times the gain from the cathode to the plate of \\. This can be written
in a single equation as
Overall gain of cathode-coupled stage
= _ g^TL(TL + rp)[l -f (rp/ra) -f rpgm] _
J2(l + rpgm) + [<rL + rpj /rfc] -f ri,[(l/r,) -f gm}\^
SUPPRESSOR INPUT, SCREEN OUTPUT AMPLIFIER, The circuit for this ampli-
fier is given in Fig. 37. The circuit requirements are
as follows : the tube should be of a type that normally j *""*" v
operates with the screen at a lower voltage than the
plate, and also it must have a suppressor grid struc-
ture that has an effective mutual conductance to the
plate. The 6AS6 is a satisfactory tube for this type of
operation, as the suppressor-grid-to-plate has a mu-
tual conductance of about 1000 micromhos, and the
suppressor grid-to-screen-grid has a mutual conduct-
ance gms of about 850 micromhos. The screen im-
pedance Z, is of the order of 10,000 ohms.
By the use of a 6AS6 for an in-phase amplifier, the
values shown in Fig. 37 give satisfactory results.
Care must be taken when operating a tube in this
manner not to exceed the screen dissipation.
The gain A to the screen is given by eq. (3) using r, in place of Z and the screen im-
pedance Za in place of rp; the equation then becomes
Gain A = (62)
Tt -J- ^*
where gms is the mutual conductance of the suppressor 10 the screen.
9. NEGATIVE-FEEDBACK AMPLIFIERS
In the negative-feedback amplifier a voltage obtained from the amplifier output is fed
back to the input in such a way as to oppose the applied signal.
There are two general types of negative feedback. The first is negative voltage feed-
back which occurs when a fraction /3 of the output proportional to the voltage across the
output load is fed back to the input. The second is negative current feedback, which
occurs when the voltage fed back is proportional to the current through the output load.
The major difference in the results produced by voltage and current feedback are that
negative voltage feedback results in a reduction of the effective internal resistance of the
amplifier, whereas negative current feedback produces an effective increase in the internal
resistance of the amplifier.
Owing to the effect of reactance in the circuit, the voltage which is fed back may not
be wholly out of phase with the input voltage. This phase shift is likely to occur at ex-
tremely low or extremely high frequencies. In a single stage it cannot exceed 90°T which
results in no feedback and a corresponding increase in gain. When more than one stage
is included in the feedback amplifier, the phase shift may exceed 90 °, which results in
regeneration and perhaps oscillation. The method used to combat this phase shift and
resulting oscillation is to make one stage with a narrower band width than the others.
This should result in a loss of gain through the narrow stage to a value at which oscilla-
tion cannot occur, by the time the phase shift has exceeded 90°.
The effects of negative voltage feedback are (1) reduction in gain, (2) reduction in dis-
tortion, (3) reduction in noise, (4) improvement in the fidelity with frequency, (5) greater
consistency of characteristics with changes in applied voltages, and (6) reduction of the
effective internal resistance of the final amplifier stage.
The gain or amplification in the presence of voltage feedback is given by the relation
Gain with feedback A' = , A ... (63)
1 — Ap
However, for negative feedback $ is negative and the relations become
Gain with negative feedback A' = a (64)
1 -f- j$,p
which is a reduction in gain from A, the amplification without feedback.
7-52
YACUUM-TUBE CIKCUIT EUEMENTS
When the value of A w large in comparison to 1, the gain becomes practically inde-
pendent of the amplifier characteristics, becoming approximately A' — l/£.
Negative voltage feedback reduces the non-linear harmonic distortion produced in the
amplifier for a given output voltage according to the relation
(IX) Distortion with negative feedback - R (65)
1 -p Ap
wikere JE> is ti*e distortion with no feedback. This assumes that no distortion is produced
wb« reamplifving the distortion voltages fed back, which is quite accurate if the distor-
tM» with no feedback is not large.
Feedback will reduce the distortion up to a certain point, but feedback cannot increase
the power-output capabilities of a given amplifier. The distortion will be low over a
portion of the output range but then will increase faster than for an amplifier with no
feedback (Fig,. 38).
Relative Power Output
Fio, 38. The Effect of Negative Voltage Feedback on Distortion
Negative voltage feedback will improve the signal-to-noise ratio, if the source of noise
k m the amplifier and not fed in as part of the input signal. For this case, assuming equal
Signal to noise with feedback _ A1
Signal to noise without feedback ~ Az(l -f- Ap)
(66)
4j is tlie amplification from the point of introduction of the noise to the output
with negativfc feedback, and AI the amplification from the point of noise introduction to
tte cmtput wHIioQt feedback.
With »£g»f tv* feedback, as tli* response starts to drop with either high or low frequency,
the £e«dfeaefc also decreases, opposing the change and resulting in a flatter frequency
***MB***s**aM1' Tfcus
(67)
Gam at/2<^t) ^4S{1
f ) feedback causes an apparent reduction in the plate resistance of the
. em a feedback amplifier. Hie actual plate resistance rp does not change
j aay impeduM mataunc (as with an output transformer) should be done on the basis'
of DO feedback. Ifcen. with feed^ck, the response and damping effect as on a loud-
9^t®T TWOQAOM is the mm® m though the plate resistance rp were lowered to r ' The
dfotiv* pl*U r^^we« r/ is i|» same whether the feedback is over a single stage or
, provided (he g»ia reduction is the same,
i by
I + (i/rf) - r+T^ (68)
s with negative voltage feedback applied to a single
NEGATIVE-FEEDBACK AMPLIFIERS
7-53
The gain of such an amplifier, A', taking feedback into consideration, is given by
Af = 1 A. (69)
1 — Aa
but, since a. has a negative sign for negative feedback, eq. (69) in reality should be
A' ~ rri^ <70)
where a. is the ratio of the feedback resistor rn to the load resistance TL, and A is the am-
plifier gain without feedback.
FIG 39. Typical Negative Voltage Feedback Circuits Applied to a Single Stage of Amplification
The effective plate resistance rp' is given by the expression
TJ = rp(l + gmrn)
(71)
where gm is the mutual conductance of the amplifier output stage.
The increase of input resistance is similar to that obtained with a cathode follower,
Equation (48) will give the effective input resistance; Tk should be replaced with rn.
The input capacitance is given by eq. (46) by replacing r* with rn. Equations (46) and
(47) apply to current feedback over a single stage.
. Figure 40 shows some typical circuits with negative current feedback.
THE OKE-SHOT AMPLIFIER. The one-shot amplifier is a form of multivibrator
with one of the tubes biased beyond cutoff. The circuit is shown in Fig. 41 . Under steady-
state conditions tube Vi is cut off and tube V+ draws plate current. The circuit remains
in this condition until a positive trigger voltage of sufficient amplitude to cause Vi to
T-54
VACUUM-TUBE CIBCUIT ELEMENTS
Fw. 40. Tjrpiml Nf«»4iT* Cmrreat Feedback Circuite
current
charging the coupling ca-
pacitances Ci and C2, result-
ing in a large negative po-
tential on the grid of FI.
As soon as the current in the
plate circuit of Vi stops in-
creasing, the voltage on the
grid of F2 starts to rise; this
is also regenerative, and Fa
resumes its steady-state
plate current, but Vi is left
with its grid highly negative.
This negative voltage dis-
charges through rj. exponen-
tially back to the applied
bias voltage J&, Fig. 42.
Owing to the regenerative
action the output of this
type of amplifier is a sharp
pulse of short duration. The
plate of Fi gives a negative
pulse, and the output from
Fz is a positive pulse.
The voltages acting on
the grid of Fi are shown in
Fig, 42. The trigger pulses
should be limited in ampli-
tude so that, at the desired
time after firing, the ampli-
fier is again ready to fire.
"With the trigger pulse
limited to amplitude P it
cannot fire the one-shot am-
plifier earlier than the pre-
scribed time. Assuming
that Ci and Ca are small
enough to permit them to
change to the peak positive
voltage applied, then the
operating conditions can be
calculated.
Ir «irop tbrauiift the plate load resistor n, of Fa must be appreciably greater than
cutoff voifakg* r«qiwe4 cm IV
Positive
.f B Negative Pulse
Circuit Dtagram of ft One-shot AmpiiSer
I*. 41 far
totow^toU^cuw^b^riOt
tiae trigger poise amplitude P
bias to be equal to ^i -f P/2,
PULSE AMPLIFIER
7-55
Zero Bias
HI
FIG 42. The Voltage on the Grid of Tube (TO of Fig. 41 during Operation
The time T that must elapse between firing of the amplifier and the second firing by a
pulse of amplitude P is T = r^Ci -f- C2). The applied bias — Ec to Vi of Fig. 41 is
given by:
and EB-L is given by:
BBI = Mitel* - 1-85P) (73)
where jui is the amplification constant of V\, and r^/p, the voltage drop across the plate load
rz, of FA, is assumed to be the maximum negative voltage on the grid of "V\ immediately
after firing.
10. PULSE AMPLIFIER
With the advent of radar and television, pulse amplifiers became necessary. The pulse
amplifier is an adaptation of the wide-band amplifier. The bandwidth necessary is de-
pendent upon the pulse, the high-frequency response is governed by the rate of rise and
decay of the pulset and the low-frequency response is determined by the duration of the
pulse. (See Section 9.)
The equivalent frequency /2 of the pulse is considered to be equal to that of a sine wave
that rises from zero voltage to peak voltage in the same time as that of the pulse. This
results in a frequency /2 that must be passed by the pulse amplifier, given by
/. - -4 w
where T is the rise time or decay time of the pulse, whichever is shorter (see Fig. 43).
T^ u-7*-*!
H-TF TH H
Symmetrical Unsymmetrlcal
Negative Pulses
FIG. 43. Negative and Positive Pulses, Showing the Pulse Rise Time ( Tr) , the Pulse Decay Time (2» ,
and the Pulse Duration (Tz>)
Determine the frequency /a represented by the rise time, then refer to the section on
wide-band amplifiers and determine the design of an amplifier having the required high-
7-56
VACUUM-TUBE CIRCUIT ELEMENTS
-E.
_l/p<ots* input
*H
(a) ^®p»r*i*nt potat for
•Ovtpvt
FWL
44. Grid! Bias, Plate Curreat Curve,
im« tfee Operating Point £«<• * Positive
, tto Opvnrtu* Ptatn* fw a Ne&mtiTfc PuJsse,
a Cirroit Th*t Witt AutMftftticaUy Set the
»l tibe ProfNPt Voltaot for Correct Opera-
®| th* Fyalw Polarity or Ampli-
tude
frequency response. The low-frequency re-
sponse at 5/i needed is obtained from the pulse
duration Tz>-
fl = JL (75)
Again refer to the section on wide-band
amplifiers to determine the constants needed
to produce the required response.
The consideration for the initial bias point
for the vacuum-tube grid is somewhat dif-
ferent in pulse amplifiers from what it is in
conventional amplifiers. For a positive pulse
a high bias is needed. This bias can be,
and usually is, supplied by grid current (Fig.
44, Ai). ' _ .
For a negative pulse a low bias is needed
and the tube draws a heavy current except in
the presence of the pulse which drives the
tube grid toward cutoff. This is shown in
Fig. 44, As.
The circuit shown in Fig. 44, J5, is ade-
quate for either a positive or a negative pulse
amplifier. The time constant of the grid
circuit rjCi should be several times the pulse
repetition rate to maintain bias between
pulses.
With positive pulses the grid is biased by
means of grid-leak bias to a value represented
by the a-c axis of the positive pulse. This is
self-adjusting and requires no controls. When
one is operating with negative pulses, the bias
will be essentially zero, depending upon the
pulse a-c axis, and will operate equally as
well as for a positive pulse. A circuit of this
type is self-adjusting and assumes an operat-
ing point so as to provide efficient operation
regardless of pulse amplitude or polarity.
^ (I-JF) AMPLIFIERS
By Charles J. Hirscfc
to amplify and separate signals at high radio frequencies, some
the signal frequency to a fixed intermediate
it m
(kucwii &i
Ttif> Mcn*l tfcMMH ia mmtpliSed arid selected at the new frequency by means of an
i~/ oMjRlv$*r. Ssadb rwwtwrs differ from tuned-radio-frequency (t-r-f) receivers, which
amplify by maaas of eibreiiit® tun&d to the high carrier frequency.
Th* mtenoMNltttto frw$u&eney is usually lower than the radio frequency and higher than
tlwi tnega*ncy of utiBsaAkm (audio or video frequency).
Th* »ieriiM»Ai»4«»-lr^qp@iic^' ampliiser has the function of amplifying the signals within a
ipmifd s-f band m®& erf rej^ctia^ all others. It is the most important factor in the deter-
of •encttivitjr. sefectivity, and fi<felity of superheterod>Tie receivers. Since these
e eonapl®^ r«K^iv€i* are, ia the main part, tite characteristics of the i-f
to maie th*rn ooDstam over the tuning range.
UL PACTORS JJPfBCTHIG THE CHOICE OF INTERMEDIATE
FREQUENCY
Tl» A«^w of imtem*«diat« fnquency rec^res a careful study of the following factors: (1)
weraH gMft, (& wlMtivity, C3? i»^e rej^ctMm., (4) tuning range, (5) tweets (whistles caused
by faurvMHUNMol tb* i-4 «H»db am a»n*r»t*d % Hit sec€»d<^eetorand reimpressed on ther-f
wnn-1* to b«ai with tb» ««Aml frequenej*), (6) i-f re|©ctiois, (7) strong stations separated by
, (8) ©oa, i^., number ol t«iw>d <arcwits and their components.
FACTORS AFFECTING INTERMEDIATE FREQUENCY 7-57
Low intermediate frequencies have the advantages of (a) high stage gain because a
higher impedance can be presented to the output of the amplifier tube; (b) narrow band
width, i.e., better selectivity because a given frequency separation is a greater fraction of
a low intermediate frequency than of a high intermediate frequency (see Universal selec-
tivity curve, Section 6) ; and (c) greater freedom from tweets (when the i-f amplifier is pre-
ceded by a high degree of r-f selectivity) because only higher and therefore weaker (but
more numerous) harmonics of the i-f occur at the signal frequency and beat with the
signal to produce tweets.
High intermediate frequencies have the advantages of (a) higher irnage rejection by
(1) increasing the separation (twice intermediate frequency) between the desired signal
frequency and the image frequency, and (2) reducing or even eliminating that part of the
tuning range within which signals can produce images; (6) reduction in the number of
"tweets" because fewer harmonics of the intermediate frequency lie within the tuning
range; (c) greater freedom from "birdies" (whistles produced by combinations of r-f sig-
nals) because combinations of r-f signals, separated in frequencies by the intermediate
or subharmonics of the intermediate frequency, will not be impressed on the converter to
produce intermediate frequency, or beat with the local oscillator to produce intermediate
frequency; (d) greater freedom of interaction (pulling) between the local oscillator and
the antenna circuit because of greater frequency separation.
High image rejection and freedom from "birdies" require costly r-f selectivity. There-
fore, a high intermediate frequency is economical because it reduces the requirements for
r-f selectivity.
The i-f amplifier frequency must not be too close to the tuning band as the receiver will
then become unstable.
Table 1 presents a comparison of the receiver characteristics associated with two inter-
mediate frequencies for the broadcast band; Table 2 gives some idea of the intermediate
frequencies commonly associated with specific radio frequencies.
Table 1. Comparison of Two Radio Receivers Having (a) an Intermediate Frequency
of 175 kc, (6) an Intermediate Frequency of 455 kc
Tuning Range 550-1720 kc
i-f
I75kc
i-f
455 kc
1. Frequency separation between desired
station and image
2. Frequency range in which stations within
the tuning range can cause images
From
To
(Note: The ability of stations outside the
tuning range to produce images must not
be overlooked.)
3. Frequency range of stations which may
be interfered with by images produced by
stations in the tuning range. (See above.)
From
To
4. Harmonics of the intermediate frequency
occurring in the tuning range
5. Separation of stations capable of beating
with each other in the first detector to
produce intermediate frequency
2 X 175 = 350 kc
550 -}- 2 X 175 - 900 kc
I720kc
550 kc
1720 - 2 X 175 = 1370 kc
4th, 5th, 6th, 7th, 8th, 9th
175kc
2 X 455 - 910 kc
550 4- 2 X 455 = 1460 kc
1720kc
550 kc
1720 - 2 X 455 = 810 kc
2nd, 3rd
455 kc
Table 2. Examples of Usual Intermediate Frequencies
Tuning Range, Me
(a) 0.150-0.275.
(6) 0.150-L720.
(c) 0.540-23.0.
(d) 40-50 Me F-m
(e) 88-108 Me F-m
CO 54-88 and 174-2 16 Telev
(g) 200 Me pulse, communication,
(fc) 1000 Me and up
Intermediate Frequency, Me
0.130
0.455-0.465
with some European receivers at 0.260—0.360 to
gain more selectivity
0,455
Some receivers use 0.455 Me for the whole fre-
quency coverage. Others switch to an i-f of 2
Me when receiving signals above 9 Me.
4-5
10.7
20-30
(21.75 sound — 26.25 picture)
H. 7-15-30
30-60 Me
f-58
VACUUM-TUB!! CIRCUIT ELEMENTS
1*. NARROW- AND MEDIUM-BANDWIDTH I-F AMPLIFIERS
I-f wnpKfim am be etasiified into (a) narrow (10 kc) and medium « 200 kc) band-
width, md (&l wkto-bftndwidtJi (> 300 kc) amplifiers. . . .
Hmrrew- aad medium-bandwidth i-* amplifiers, which are used in most receivers receiving
audio f iwmraty »-m m f-m isitettipmee, usually consist of individual stages using pairs of
cotipfed-tuned cimaita. A rwtanguiarty shaped selectivity curve (one having a flat top
ami ataap «3®*t usually i* desirable-
AMPLIFIERS FOR A-M BRQABCAST RECEIVERS. These usually consist of
&* critically omipW, <k>yble-i*med stages at a frequency between 455 and 465 kc.
4250 v
IVyfeal 14 Amplifier for iaeipensive 550-1720 kc Receiver
is affected by the need for (1) gain, (2) selectivity, (3) fidelity, (4) stability,
{&) vDoutaHny.
Gala aad S^^^trl^. Tbe i-C aaapH^r k tfee major source of gain and selectivity in
& radio nmaivftr. The l-f span (froiu radio frequency on the converter grid to the second
dtotoctor) dbpeffA eta tho perfonxiaaee required. It will lie between a rmmnnnm of 1400
for «fj®4m^dl (aaualbr SS6~1750 kc) sets having a high gain r-f stage and large r-f pick-up
tip to & auudmtmi ®£ 50,000 lor rtwrt-wmv« sets with small r-f pick-up and using low-noise
«3»?wt#r tubia. For ffiiagb-foaiid sets it is seldom necessary to use more than one i-f stage
I© yet the r«*niir@d gam aad sei^Jtivity. In general in such cases (two i-f transformers, see
F%. 1) tba ^a»e «a«® nomfe be M|£i. TMa reciuire® high-impedance transformers which in
Mtra l»plii«s !$%ii -t/C r»t^ aisd hlgji Q circuits to gain the required selectivity (see eqs.
Tva^aiii I-f Amplifier U
+1CX3 w -1-250 v
^x Tmsed Circuits
«tM»).
(pb
TU Q m saad* ludi by using (a) lit* wire, (5) iron-core coils, (c)
A, aud (ili large shield cans.
tnti gain are required, and in general for multiband sets, two
^dxtoeddrcuiHseeFig.^. Tte gain and selectivity of
e^ (I^^IS) befew. Values for typical sets are sliowm in TaHe 3.
NARROW- AND MEDIUM-BANDWIDTH I-F AMPLIFIERS 7-59
Table 3,
Average Stage Gains and Second Detector Sensitivities for Different Types
of Broadcast Receivers Produced between 1934 and 1946
^^^^^ Gain
Type of Set ^^\^^
Conversion
at 600 kc
v
1st i-f
V-
2nd i-f
V
Overall
P
2nd Detector Sensitivity
Will Produce
i-f Volts
30% Mod.
a-f Watts
in Voice Cofl
30
23
43
32
39
40
26
14
44
39
35
10
37
94
61
88
44
56
100
56
41
120
90
2,800
1,400
2,800
50,000
2,200
4,000
14,300
21,000
5,300
3,500
0.3
0.3
0.5
0.5
0.5
0.6-0.9
0.6-0.9
0.6-0.9
0.7-1.1
0.7-1.1
0.05
0.05
0.05
0.05
0.05
0.50
0.50
0.50
0.50
0.50
Ac-dc (r-f gsin of 6)
Battery (no r-f stage)
(no r~f stage)
(r-f gain of 10)
Ac (no r-f stage)
(no r-f stage)
(r-f gain of 1 2)
Auto (no r-f)
(r-f gain of 40)
If two i-f stages are used, the overall gain can be held down to reasonable values, stabil-
ity can be improved, and the cost can be reduced by using (a) solid wire coils instead of
litz as the five or six tuned circuits will supply adequate selectivity even with the lower Q
of the solid wire coils (6) lower L/C ratio, (c) output voltage obtained from a tap on the
secondary (but not in the stage feeding the diode, as a condenser across the diode load is
necessary to present a low reactance to i-f harmonics generated by the diode), (d) unby-
passed cathode resistor, (e) increased bias (however, this decreases the effect of avc on
this tube).
Gain and Selectivity of Last Stage. The gain of the stage feeding the avc diode must
be high enough so that its own grid will not overload owing to inadequate gain control of
the preceding stage. In other words, it must, without overloading, supply enough power
to the diode so that the diode may supply adequate control voltage to the preceding stages
for all signal amplitudes to be expected. For remote cutoff tubes 30 to 40 volts of avc
may well be needed, which represents from 60 to 85 per cent of the peak carrier voltage
impressed on the diode.
The ratio of a-c to d-c diode load impedance should be as near unity as possible to
prevent amplitude distortion on high percentage modulation signals.
Variable Selectivity. (See reference 4.) Extreme selectivity usually causes extreme
cutting of the side bands with loss of fidelity. To overcome this, some receivers use varia-
ble selectivity. This usually is obtained by coupled circuits which are critically coupled
(or undercoupled) when selectivity is required, but which are overcoupled when selectivity
can be sacrificed. As the coupling increases, the selectivity of each coupled pair assumes
the well-known two-peak form. The frequency separation between peaks CA — /a) in-
creases with the coupling. — = K approximately for overcoupled high-£ circuits.
Modulator
K Is adjustable frtwn
K^Kcto K>Kc
Tl
Low M to approximate
two sfngfe-tuned
circuits in cascade
13 ^-^ T4
FIG. 3. I-f Amplifier Having Variable Selectivity
The valley between the peaks is filled in by the selectivity of a single^fcuned circuit. A
flat-topped selectivity curve can be approximated for all coefficients of coupling if the Q
of each circuit of the coupled pair is equal to twice the Q of the single-tuned circuit. In
practice, the i-f amplifier takes the form of Fig. 3t which consists of three double-tuned
circuits. The coupling of the first two pairs is adjustable and capable of being overcoupled.
7-60
TACUUH-TUBE CIBCUIT ELEMENTS
The waging of the teat pair k low so as to approximate the selectivity of two single-tuned
circuit* m eaueade Cos* to M in the valky of each overcoupled pair). The Q of the adjust-
able pain to equal to twiee the Q of the very loosely coupled pairs. The cathode resistors
of shout im ohma ar* unbypaaeed to minimize the detuning caused by variation of the
fetus by the arc, {3e# reference 3.)
BrtMbd i-f ampttfierB are sofnetimes used to reduce the need for frequency stability in
the local asettl&tor in pushbutton aeta or short-wave sets.
Ttoatag Stm&Ilty. The amplifier should be tuned with enough capacitance (> 25 yujuf) so
thai it will not be appwtaMy detuned by (a) replacement of tubes, (6) displacement of
p*rte by Tifaratioa, (r) efaaag* in input capacitance of vacuum tubes caused by variation of
gun. CTtii emu fe« ImiMsced fey a Sinai tinbypassed cathode resistor (reference 3) of about
HX> ohms; ssw? Fi«.
Bamiwlrftha
Bami width at 6 db
coupling to be slightly
below optimum
^^
~~2*7 '-1"'
p« la t« b« !M»| » mtobnwii by 3*pa*»ti*»« plate & grfd leads
Me 14 Transformer
r will rawi wkk Taiiatkjns in temperature and humidity, the use of
stable ix€»d uow^aaers »ad tmiBf by meiuis oi adjustabie iron-core coils is desirable.
The is*dy itiw ooupliac few ween wmdiags caa either aM or oppose the coupling due to
the eap«cii«a<* fe«twe«a the pl»t« and gr»i terminals of the i-f fe-ansformer.
II vety «a^ traiwlormers M« dewred, opfxieing inductive and capacitive coupling
ptroits ciowr apaan« of the winding. F<r coaxial coils, wound in the same direction
permit the o«k to be partly self-skidded eiectrostaticany by usin^
as th# fow i-f poteatial terminals. ^^
ia th«s ate^c mp»eitaiice, due to differences in production wiring
®ttw®®11 w^®8 *» to vitedik», causes much larger variations in the
" ^ SSUe with ^^J^0^1^ «^l^ags than with aiding coupling
quanfeities variee much ^^r6 thaa their sum
ccm^ing AoiiW be sufficiently below
fc «• prr^wt ww««»^te« due to production variations and vibration.
NARROW- AND MEDIUM-BANDWIDTH I-F AMPLIFIERS 7-61
With either coupling, production will be much more uniform if the eapacitive coupling
is made as small as possible (see Fig. 4).
Feedback of I-f Harmonics. The second detector output must be well filtered and
kept as far as possible from the r-f components so as to prevent harmonics of the inter-
mediate frequency from being impressed on the r-f circuits where they can beat with the
signal and cause "tweets."
I-F AMPLIFIERS FOR FM RECEIVERS. The same considerations hold for fre-
quency modulation as for amplitude modulation except that:
1. Bandwidth must accommodate maximum signal frequency swing so as not to cause
amplitude distortion.
2. Gain must be adequate to operate limiter on weakest signal.
3. Top should be reasonably flat so as not to overtax limiters and to reduce distortion
in balanced detectors.
3a. Bandwidth at least Table 4. Typical Dual I-f Amplifier Stage for Am-Fm Set
150 kc at -6 db. Adja-
cent channel attenuation
±400 kc at least 50 db.
4. Selectivity curve
should be symmetrical.
5. Intermediate fre-
quency for the 88-108
band is usually 10.7 Me.
6. Amplifier consists
usually of sets of double-
tuned circuits.
7. A-m and f-m circuits
usually are combined in
one common shield can
(but care must be taken to Note: The ratio of the bandwidths of two signals 20 db and 6 db
prevent interaction SO stronger than the signal at resonance is a measure of the coupling,
that leads will not change ™s is indicated as W^fW, and is equal to 2^37 when LiCi - £2C2,
v , j j- Qi == <?2, and the circuits are critically coupled. When Qi ^ Q* as in
couplings by adding ca- atramformerfeedingadiodefexperienceilldicatestbat this ratio should
pacity between windings) . ^ 2.7-3.0. When the transformer is used in the plate of a modulator
8. To prevent detuning tube, the ratio should be 2.5-2.6.
with avc, those tubes
which have avc may be supplied with an unbypassed cathode resistor of about 100 ohms.
9. Tuning usually is accomplished by means of iron slug to increase the stability.
A typical design is given in Table 4 and Fig. 5.
Each coil adjustable
from 4.2 to S.4pl)5s
Nf=:lO.7 me
AM
FM
Frequency
0 455 Me
10.7 Me
L! = Lz
adjusted by iron core from
862 pA
4.2 tih
to
1395 jih
«.4 jih
Q .. . ...
68-77
88
K
0.70 approx.
0.80
Kc ' *
Gain
43 db
28 db
We .....
13.5 kc
215 kc
W+Q . . . ....
36 kc
540 kc
WM
2,66
2.50
We
+250 v
FIG. 5. Typical 0.455 and 10.7 Me I-f Stage for Combined A-m and F-m Receive
7-42
TACUUH^TUBE CIKCUIT ELEMENTS
TOEF0L REUITIOHS IOR HIGH-(? CIRCUITS.
Selectivity oya be expressed in two ways:
\#; With ecnstant input aa
^ Output Toitaga at any frequency / (or bandwidth /» — 2}/ — /ol)
"* Output voltage at the resonant frequency /Q
«* & number less than unity
(I) Wish ean0Uiftt output as
.
*" 5 *"
vohagg at any frequency' / (or bandwidth /» ~ 2|/ —
Input voltage at the resonant frequency /o
-= a number larger than unity
(1)
(2)
resonant frequef»cy
band wfdJh at any value oCA
(same units asjg)
h at a <&'s
K*W/t
ivcl
^rz | **T*
o[ '«
, <at c
' i-O t
<t», |8
— >w—
>
>t, «*
»
! f A/ ^ror5M»w:"tafraal»
% I* =7^- ffocdemblerBnedoirctftts
T XsjJ »adK=lCe
wkSth (j^/2) multiplied by Qj6^
1012 2 8
1
Vali
»s sf haH bar,d
3 " 2
„
A*£*
//•
<^~~
"*N-
1 *
I -
\,
ir
1 5:
\
-2
101
-€
(
15-
-4
^
-6
-7
-8
-9
\
7
A
\
^^vity, A, d m«^e do«fc4e-tuned stage i&
R^onaiat Ireqoeacy
to 8%2*1 3 db greater than resonance A/
3 db greater than the signal applied at
(3)
> resonant
WIDE-BAND I-F AMPLIFIERS 7-63
2. Selectivity - S = Signal at / (or /-/,) = i_
Signal at /0 A
(See Section 6, article 1, for universal (5cx)
h
3. Gain per Stage
G = gmQX (6)
4. Stage Gain Multiplied by Bandwidth at 3 db
(a) One stage
G Au = £m/C (7)
(6) n stages
» = — — — (approx.) (8)
Vn c
B. Double^tuned Stage (Fig. 6).
The following formulas hold when LiCi = L^C^ Qi — Qzi £ — coefficient of coupling;
Kc = critical coupHng coefficient.
1. When K ^ JTC, then, for each stage,
. Resonant frequency _^1 > n
Bandwidth to signal 1 db greater than resonance /c^ ~
Bandwidth to signal 20 db above resonance _ WSQ ^
Bandwidth to signal 6 db above resonance Ws ~~ ^
2. Selectivity, S
(a) K^Ke
_ Signal at / (or / - /o) ^ j_
Signal at /o A
(11)
(See Section 6, article 5.)
(5) K = K
S =
3. Gain per ^toge, (?
(a)
(6) js: = xc
G = V^mQX (U)
4. 5to^€ (?azn Multiplied by Overall Bandwidth
(a) One stage
G AOJ * 0.707 —• where C is the actual timing C and is Vs of total C (15)
C (approx.)
(&) n stages
13. WTDE-BAKD I-F AMPLIFIEI^
The amplification of video signals such as are used in television and pulse communica-
tions requires band widths wider than 200 kc. Hence techniques have been developed to
design much wider band amplifiers of high overall gain. One special problem arising is
VACtJUM-TUBE CIRCUIT ELEMENTS
tUft much of their use is for dually displayed information where the phase distortion
intiwfemd by a rectangular-topped selectivity curve cannot be tolerated. For this rea-
mm, the *dam of the selectivity curve must be somewhat rounded. ^
<BKJI A1WE DESIGNS. Wide-band amplifiers may be designed using (1) syncnro-
aatttfr ti*B©d Miicfe-umed ctrcuite, (2) double-tuned circuits (loaded either on one or both
•idea. (3) 9*agger~tui»d amplifiers, or (4) inverse-feedback amplifiers. Stagger-tuned
amptiftm eonwrt of a sm^-tiuwi circuits of poor skirt selectivity which are tuned to
diffmnt f reqwums to that the pe&k of oee circuit tends to fill in a deficiency of the others.
F«r touaee a ptacger-ttiaed pair consists of two single-tuned stages, one of which is
pmk#d at a frequency higher than, the other lower than, the center frequency of the
•mpli&r. la in^m-feedback amplifiers a fraction of the output of a single-tuned syn-
oiarmmm amplifier is fed back in degenerative phase to the input. More voltage, there-
fore, ia fed Imrk at rfjson&nc*? tlmn o&-re80nance. Consequently, the overall gain is reduced
mew at r®mm®&@® than off, and the nose of the selectivity curve is rounded.
FIGURE OF MK11T, The Sgure of merit of a wide-band amplifier is defined as
Stage gain times overall bandwidth — G A&?
w^ft the band width Ju^ means the band width for gains 3 db below the peak. The 3-db
land width is ehoeen because it makes the mathematics easier, it approximates the noise
hfttt'iwidth erf the rweiwr, and so facilitates signal-noise comparisons. Furthermore,
with the usual ©owpting circuits, the rise time of pulses is quite simply connected with it.
Defhunc m* tiiM m th* time required for the response to the step function to increase
frori 10 to 90 per cent of its final value, then
0.7
Hise time =* —
Tlmm » 10-Me (S db dbwa) i-f &mpliSer would have a minimum pulse rise time of 0.07 jus.
(For * €M»aplH@ eritemts of a puke amplifier, percentage of pulse overshoot must also be
<tMQtaidtf*d. )
For m ^mgl^^tage single-tuned circuit the gain of an amplifier is (Z is the plate load
^m ^ gm
— — - —
(17)
i is aho eq. (7). Tb* fawelor C represents the total capacitance in the plate circuit,
infiudi&g tube output and input capacitances and the capacitance of circuit components
to fproufid.
Since double-tuned nroaits divide the total tube and circuit capacitance between two
tuaed (ircuita they use fe«s capacitance per tuoed circuit and have a higher figure of merit.
For equal Q*» this m VI g»/C, asd for ®m side loaded it is 2gm/C.
STWCHROKOIFS STH GLE-TTJHED CIRCUITS.* The sim-
OveriS ptkity a®d stafeiity of an amplifier ma<fe up of single-fcuned circuits
@| aU tuned to resonance oommeiid it to the designer, and most 2- to
j si y S-McHwkle amplifiers are of this type. For really wide-band high-
i Amplifiers pan mmpMfkra the decrease in bandwidth arising from multipli-
cation ol the successive selectivity curves makes this type unsuitable.
Table § shows th« overall bandwidth of it-stage amplifiers in terms
ol the %&m®e bandwidth. It siiows that a nine-stage synchronous
^^jie-t^acd amplifier with an overall bandwidth of 4 Me requires
a singliHstAge baadwMth of 14.3 Me with its correspondingly low
g»wa. It eaa be shown that the maximum overall bandwidth of syn-
Aroamii ^agle-tuaed circuits occurs for a mean stage gain of
g - V*~= 4.34 db
DOOTI^-TUHED CIRCUITS. Double-tuned circuits have a
ita«« in the figure of merit. However, the large
-^^jfeaents (three per stage) and the criticalness of
i) make desagn and maintenance most difl&cult. For this
fern Jaeea wxsd vwry little.
CmcuiTS. WaBman defines an exact stag-
geoiaetricaBy centered at/* as consisting of i
*" J ~ l/Q and :' * - -
WIDE-BAND I-F AMPLIFIEBS
7-65
(for one triple) (6) one single-tuned circuit of dissipation factor 5 — A/// centered at /Q.
d and a are plotted as functions of 5 = A/// in Figs. 7 and 8. (Note: The values of d and
a for a pair are not the same as their value for a triple.)
The stage gain times overall bandwidth of (a) a single-tuned stage, (b) an exact stag-
gered pair, and (c) an exact staggered triple is
G S = gm/C
However, the same 3-db bandwidth AOJ is obtained in the first case (a) for one tuned
circuit; in the second case (b) for two tuned circuits, and (c) for three tuned circuits.
/•
0 fi
j
/
1 9
/
i R
/
/
/
X
1 6
/
^^"^
^
1 ^
/
S
^
^t***
1.4
1.3
1.2
1.1
1.0
0.9
0.8
0.7
06
0.5
0.4
0.3
0.2
0.1
Ex
act value o
|
ee-.
<S
?/
^
^
1
J-d
^
^^
1-h.
Asym
353 1
ptotic
fors
sof^
'
valu
mall
/
/
s".
^
of a.
jfaluq
/
^
^
2^
s
/
^
^
„*•-'"*
/
s
.
^
/
^<
•^
/
/
^^
^
0.7075
Asymptotic
valu
/I
^
Exi
ct va
ue of
J
of d for small
values of S-\_
s
^
^
st
V
S
/
s
/
S
/
/
f
0 0.1 0.2 0.3 0.4 0.5 0.6 0.7 0.8 0.9 1.0 1.1 1.2 1.3 1.4 1.5 1.6 1.7 1.8 1.9 2.0
PIG. 7. Design Curves for an Exact Flat Staggered Pair
The algebra in the analysis of these circuits is quite involved, but Wallman has reduced
the design to charts. Given the tube type and the general layout, the gm is known and
an estimate of C is made. This determines the product of swgknBtage gain and ov&raJl
bandwidth, i.e., G Aw = gm/C of the pair or triple.
The overall bandwidth of the amplifier can be obtained from the following approximate
relations _
_,.,,, . Bandwidth of one pair (i.e., Aw)
1. Bandwidth of n pairs = - 4-^ -
1.1 n
2.
Bandwidth of n triples :
Bandwidth of one triple (i.e., Ao?)
1.06
7-66
VACUUM-TUBE CIRCUIT ELEMENTS
23
2LJL
2.1
13
U
UB
1.4
3-3
UZ
1*0
ex*
CUB'
OJ
0,6
0J2
ft 1
1
/
x
x
x
X
^
X
^
^
Ei»
:tv*l
je Of
a-^
x
^x
^
^
X
.<^
X"
^
x
^^
^
Asymptotic v
)ue
j
S
^
X""
of Of for sma
values of 5
^
\J^
+>
^
r"!
^
^
^
^
^
^
^~~~
faym
tfdi
rtvu
^Dtk
of srr
wk»
*9
^
^
^^^,
^^
*~~~
. — •
4
1
V
^*
^ —
\ \
~Lx
x^
^<
-Exj
ct va
ueof
d
\
<^
ss^t
•^*
A
X
x
^
<^
\
,
0 CU 02 08 CL4 05 06 0.7 0.8 03 1.0 1.1 1.2 13 IA 1.5 1.6 1.7 1.8 1 9 2
Design Cianros for &a Exact Staggered Triple
Cwwtrvtfcr, tfe« oreral! fe^kdwidtfe and oT^all gain being known, the number of stages as
vsaiA p«siioriaifcaee can be determined.
Tte •t«ci
1(^ db '^^^ <» 30 Me is wanted. 6AC7's
total capaciUnw ^ 25.5 ftpl aje to be used.
» 108 t - 12 «fb, ysat ie, a voltage »aia <^ 4 times.
- X 1013 - 3^ X 10»
^^Mii tiivii *re ftmsd ta^ H«. Sw
WIDE-BAND I-F AMPLIFIERS
7-67
II
s §
li
.£
"?
7-48
VACUUM-TUBE CIRCUIT ELEMENTS
Use Hftatiaer, therefore, • made tip of three triples, each of which consists of:
1. One tirewt tuned to 30 X 1.21 - 36.3 Me and having a Q of 4.65.
2. Otw eireuit tuned to 30/1.21 - 24.8 Me and having a Q of 4.65.
3. €fm ctreuil tuned to 30 Me ami having a Q of 1/0.443 =» 2.26.
» Q « «Cft (K in thw ewe k the equivakaat resistance across the tuned circuit), then
Q 4.65 __ ^ 79Qw for the 36.3.MC circuit
* 2* X 24.S X 10* X 25,$ X I®
— « 1150w for the 24.8-Mc circuit
i— 12
2.2®
X 30 X
X lO
___ M 470<d for the 30-Mc circuit
i-19
Tbt awis^w » sfcowa in Fig. 9. Actuallj* the physical vmloes of the shunting resistors are higher
this* a»le«kf«d bwmw*- ^ the effort of tube loading and of the finite Q of the coils which effectively
thuat tfc* j*>nwa iwwtor to the eakuUted value. The final value of these resistors must be deter-
"
ttac* Q* ^^ triple is determined from the relation
tk*t tbe rr«^» fo
i triple can be tibulited as follows:
A.M«
0
A/, Me
Shunt
Resistance, ohms
O) 54.3
f2) 24,8
«3) M,©
4.65
4.65
2.26
7.9
5.4
13.3
790
1150
470
tables which extend tlie dmgn to quadruples, and so forth, called
IHTERSE FEEDBACK I-F AMPLIFIER CIRCUITS. Typical feedback
drain* are abown isa Fig^ ICte, 1(M>, ami lOc, These are drawn without regard to d-c po-
MkBtial^ TfciM ttoe grkli imiai foe protected from the plate voltages by blocking condensers
or, pffdffmNy, IraBtforswrs hmvisg uaity coupling.
Tbe f«4b*ck Aaiia^ of Fig, ICki is ol little use, despite its high gain times bandwidth
factor, foeewist ila gpm caaaot be ecmtrolled. Figures 106 aad lOc show respectively a
fVWv
la each case the voltage which controls the
pair ami ft^dbaefc tri^e.
ii «$|)1M<1 to the ir^ tub©.
A ««»^»le i-f asapiii&r mm® 0AK5's mad imv«nse feedback is shown in Fig 11
TW» MqpMw ©mwts €^ *w^ triplati mad® up re^ectiTely of tubes V-301 V-^02 V-303
d V^W. V-^S, V-306, Gaia octroi is appfei to V-301 and V-304. This alnplifier
60 Me n^i has aa overall gmia of a^jroximately 90 db arid a bandwidth at
10 Me.
«f featecfc amplifcrs U not m readUy comfmted as that of stagger-tuned
Hwwifof® M Im^d to a greater extent on test and experience
F«r am ««^^ ««Mdy of f«*sdb»ek ampiife^ ^ rel^enoe 9, 10, 11, 13, and 14.
WIDE-BAND I-F AMPLIFIERS
7-69
f-70 VACCUM-TUBB CIRCUIT ELEEMNTS
* STAGGSR-TtJimD AMPLIFIERS VS. INVERSE FEEDBACK AMPLIFIERS. The
etew between a stagger-tuned aad an inverse-feedback amplifier depends largely on the
omim*t*xa<!*is suritmsadiiig it« use- There is no fixed answer as to which is best for all
condition*. The difference® are outlined below.
Fifmr« ©f Mftiit. Both th«e® types ol amplifiers have been shown to have a much
higher 6gura of merit than the synchronous single-tuned circuit type. Theoretically the
tov*r«e»f««db*c!t amplifier can have a higher one than the stagger-tuned, but it is difficult
to actssrrf tb» in prirtiee, » thmt they may be assumed equal.
G*is C«atr«*L Gain adjustment may be desired (1) to change the output, (2) to change
UM gain with time (pan time control, gtc in radar applications), (3) to reduce interfer-
«o«*. (4) for automatic gain stabilisation (ags), (5) for automatic gain control (avc).
A ttaiHpv^UuMd amplMiar''® bandwidth being practically independent of the tube's
I «,, gain control can be applif-d to ^115' tube.
AM tavern-feedback amplifier emu use for gain control only those tubes which are not
in tlw feedb^^k coam. Otherwi^, the bandwidth will change with gain.
Gaia Y*rimti®a witli g w. The gain varies more slowly with gm in a feedback amplifier
(approximately as i»^! than in others (linearly with gm). This means that the gain of
msBpiiSwi not equipped with automatic gaia stabilization (ags) will be less susceptible to
voltage rhaBgf, tub® ageing, and tube replacement if of the feedback type.
Kffact ^ Rc^ac«m3emt Tufees on Bandwidth. In a feedback amplifier, the resonant
frequency* and thfrefore th« overall bandwidth, is less affected by replacement tubes of
differing cmpadtsucje, Howmsr, the bauadwMth is more affected by tubes of differing gm.
; Frequeacj. An iDveree-feedback amplifier has all its circuits tuned to the
of the pass band.
Tuaiag. In a stag^r-tuaed amplifier the tuning of one stage is in-
' the taking 01 the other stage.
BIBUOGRAPBnr
1, Dfemrn, C. E%»«a^ WMtfe fWtora f®r Cswakde Tuned Circuits, Electronics, July 1941.
2, Sf*a3sl'Ai»>c» W, E»# Jr., DS^EB <3l Supcrfeeterodya® Intarniedi&te-frequency Circxiits, RCA Rev..
Apr*] 1WK
S» FnwaeMMk, E. 1*., IT*B ol F«e«fiM^!k lo Compensate fca- Vacuum Tube Input Capacitance Variation
with Bi», /We. /»JLJL| NGrwrnbes- 1 938.
4. Wl««ei*r, H* A,, aand J. 1C. Joteim, High fidelity Receivers with Expanding Selectors, Proc*
IT. H. A.« Wide Bfetml Amplifeefm, jmp«r presented at joint meeting of LR.E. and A.LE.E.
m New York, Apri IS, .
ft, Ffirt«r, R £., »ad 4F, A, Eiyalcsm, lat^Hsediatc-lrwiiiaaey Values for Frequency-modulated Wave
Rmvivft, Pr^c, /JU^, Octdfcw 1941.
7. Zwwrto, V. K.f «ml G. A. Mwton. TfimnMi, Ch»pt«r 17. John Wiky (1&40).
*• S^^Sf11* HmrirvS«M»8r-ti»«4 I-f AaBi*S«ra» R*sii»tiosi laboratory R^ort 524, NDRC Div. 14.
•, TJM T^WFJ of M A»|^&»« with Ke«j*iive Feedback, Canadian N&tiooal Research Council
.
St. UwwW^E. N^ felwM^a o« BreawS-feaad Feedback I-l Ampfifiers* CRG Report 93, Naval
ri Latbcrstory, Oct. 22, 1945.
, . , .
IL ^^W™* W" E^a^9^ fm ^v®^*^ AmpBfiats, CRG Technical Memorandum 217, Nov. 26,
W**ie Barf Am^^Nwt for T«j®rfeaw,
TAJtar attd Waflwam, FarwiMi Tulw 4
f», JM'CCjrtWW-KliS,
IZ W**ie Barf Am^^Nwt for T«j®rfeaw, J^V^tr. I.&.E., July 1939.
ii. TAJtar attd Waflwam, FarwiMi Tulw 4»»iaftM^, Had. L*bo«itot7 Series No. 18, Chapters 4, 5, and
f» 'Cjr-
MODULATORS
ByJ. E, Yimce
tto WMISS wiw^ tfee amplitude, <»• other eiiaract^Ktic, <^ a wave is
wcm® rahie of anotl^r wave. The firsfe wa^e, which is
llie "earner wave"; the second is called the
cftrrier fr^mttmcj m th*^ lrmm«ii<iT c^ the carrier wave.
i«»vtiHifrft«nMMgr tmn«is o® ea^fet side <^ the earner frequency within which
of modoli^m. In amplitude
. .
^t^wytfe o| a trmmmiinsd ^delmiMi is anally no greater than the band-
*** « a f ^^-mcHJulated sgnal is de-
^
taHMri Igr bodi tbi
TYPES OF MODULATION 7-71
Percentage modulation (amplitude modulation) is the ratio of the difference between
the maximum current (Zm) when a signal is impressed and the maximum unmodulated
current (I«) to this maximum unmodulated current, expressed in percentage, or M =
100(7 'm — It} /Is- For less than 100 per cent modulation this may optionally be expressed
as the ratio of half the difference between the maximum and rninimurn amplitudes of a
modulated wave to the average amplitude, expressed in percentage.
Percentage modulation (frequency modulation) is the ratio of the frequency swing when
a signal is impressed, to an arbitrary frequency swing which is defined as 100 per cent
modulation, expressed in percentage. The frequency swing defined as 100 per cent modu-
lation is different for various services. For f-m broadcasting, for example, 75 kc is used.
14. TYPES OF MODULATION
A single-frequency current wave can be expressed as
i = A sin («i -f 0) (1)
where A is the amplitude, co/27r the frequency (when constant), and & the relative phase.
If any of the three independent magnitudes, A, co, or 0, is slowly varied (slow in com-
parison to co/2x) the wave is said to be modulated. The three cases are called ampli-
tude, frequency, and phase modulation, respectively.
If w and 0 are held constant but A is varied sinusoidally, so that A = Jt0(l + m sin t^t) ,
eq. (1) becomes
i = jto(l 4- m sin «ii) sin (^ -f #) (2)
which, when expanded trigonometrically, gives
i = A0 sin (tat + 0) -f ^ {sin [(w + «n)t -f &} + sin [(« - «*)* + 03} (3)
The quantities in the bracket of the second term on the right represent sum and difference
frequencies of the two original frequencies. They are the sidebands. Comparison of
these two equations shows that a wave of a single frequency and periodically varying
amplitude is mathematically equivalent to a wave of constant amplitude and frequency
and a pair of sidebands.
Roder has shown (Proc. I.R.E.* Vol. 19, 2145 [1931]) that, if A and 0 are constant but
w ~ o>o(l + kf cos jo£) , the current is (let c«>o£ = tat + 6)
i = AQ sin woi + Ji(m/)[sin (coo -f M)* — sin (too — fi)t]
— JjOw/Hsin. (o>o -f 2^)2 — sin (coo — 2;*)fj
-f /3(m/)[sin (wo 4- SM)* - sin (wo - 3jn)« (4)
where m/ — fe/co/ju so that m/ is the ratio between the maximum frequency shift and the
audio frequency; also Jn(ri) means the Bessel function (see Section 1, article 14) of the
first kind and nth order for the argument m. In this expression there are theoretically an
infinite number of sidebands, although the amplitude of all those of higher order than the
first is usually negligible.
If A and o> are constant but 6 — #0(1 + KP sin p£)f Roder gives the current as identical
in form with eq. (4) except that m = KP6Q. Here, again, there are theoretically an infinite
number of sidebands, but only those of the first order are of importance or of appreciable
amplitude.
Except for some very early and ineffective attempts to use frequency or phase modula-
tion, amplitude modulation was used exclusively for communication and broadcasting up
to 1936. Exploration into the higher radio frequencies and the adaptation of these fre-
quencies to wide use for numerous services has brought frequency- and phase-modulation
techniques into great importance, since the wider frequency bands required, if they are to
be used effectively, become available as the usable frequency spectarum is extended into
the hundreds and thousands of megacycles.
AMPLITUDE MODtfLATION. Since the e2 term of the power series of development
for current in a non-linear circuit gives rise to the term sin c^t sin w£, characteristic of
modulation, it follows that modulation occurs whenever any of tfie circuit parameters c»ar#
with instantaneous voltage (or current). In particular, if it is assumed that a single high-
frequency voltage epf — E* cos (&JL + 0») is introduced in the plate circuit of a vacuum
tube and a varying audio voltage eg — 2 Esk cos (caj^ 4- 6k) is impressed on the grid, then,
I
7-72 VACUUM-TUBE CffiCUIT ELEMENTS
fa*M Be«*k» ft. mkie 21, «q. (17), the tarn* having frequencies near that of aJZ* are
»V» - :
*»*
I -
L
COS (ttj$ —
J
bt wiittaA (WHOM t&*
as iU^tmted there IE eq. (22). This may optionally
<rf *<,4jk, and *(._« negHgible as is usual in practical
tfct
Th®
(7)
ia the brmrket ia aimply the maximum value of the audiofrequency plate
ar« ahown in Fig. 1.
A.- Signal Curraisl
One Component of
the Second TerrQ
c^ Equation (5)
Tolal of Equation (5)
for Two Sine Wave.
Voltages
The Secood Term
of Equation (5)
Equation (5)vsfjlh
One Part of the
Second Term
- - - - Eliminated
F.- Carrier *mf Om S^k Band
F»fc I. Cemfeiaa^® ef Sine Wave Carrier aad ^gaal Curr^iis
METHODS Of PKOI>UCIIf G AliHJTirBl MODULATIOK. Systems of modula-
"*--•»"••••• s imto turn daa®^:
kti t^ iai|j«4aiice of * r-f oeallator, amplifier, or combination of
. l§ twwr*iNsl tsgf thfe tao^ilatiiig wave.
_t. 8v*t«m!» feaa^ym^j a eo^taBt-impedaBce r-f oscillator, or amplifier, having a var-
*a aeriea w^Jbt it in whidh the variation o! the magnitude of the series
D*- Carrier wtd Bi^fe Skie Bamh
GRID MODULATION 7-73
impedance is controlled by the modulating wave, thereby controlling the input to the r-f
unit.
The first method of modulation may be accomplished by varying the grid bias of the
r-f oscillator or amplifier if a triode is used or, alternatively, varying the suppressor or
screen-grid potential if multielectrode tubes are used.
The second method depends for its operation on the introduction of the modulating
emf in series with the plate power supply of the modulated oscillator or amplifier. Since
appreciable amounts of power are required to accomplish modulation in this manner,
auxiliary tubes are employed as modulators.
15. GRID MODULATION
The term grid modulation is commonly used to describe modulation systems of the first
class mentioned above. Modulation is effected by varying the d-c grid bias voltage or
suppressor grid voltage at an a-f rate, by connecting the modulating source, such as the
output transformer of an audio-amplifier stage, between the bias source and the r-f stage.
Since the grid input resistance is high, the audio amplifier need be capable of only a few
watts output. The power required is still further reduced in some designs by the use of a
tube in the r-f circuit which is capable of large plate currents without exceeding zero grid
bias. In this case the a-f amplifier looks into a circuit of substantially infinite impedance.
The operating bias for the r-f stage is determined as follows: The r-f tube is first biased
to cutoff, with no r-f grid voltage. The r-f grid voltage is then increased until the knee of
the saturation curve is reached. Then, with a constant r-f grid voltage, the d-c grid
voltage is increased until the plate current is substantially zero. If ei is the d-c grid volt-
age for maximum output, and ez is the d-c grid voltage for zero output, the operating grid
voltage should be (eg + ei)/2. The peak a-c voltage required from the audio stage to
produce complete modulation is (e% — ei)/2. Because of the relatively low efficiency
obtained, grid modulation methods are generally applied only where the amount of mod-
ulated power required is very small. Higher powers are sometimes obtained by following
the grid modulated stage by r-f amplifiers. The outstanding advantages of grid modula-
tion are its simplicity and cheapness, which make it attractive for small, light-weight appli-
cations, such as portable or airborne.
POWER AND EFFICIENCY OF GRID -BIAS-MODULATED AMPLIFIERS. The
following discussion may be applied in determining peak power requirements, efficiency,
driving power, etc., of class B r-f amplifiers as well as bias-modulated amplifiers, since
the tubes operate under the same conditions in each ease. The peak power output capa-
bility of the tube must be four times the carrier power if complete modulation is to be
obtained. This follows from the fact that the output current and voltage must be doubled
on peaks of 100 per cent modulation. The efficiency is proportional to the percentage of
modulation, and it is of the order of 20 to 33 per cent for normal carrier or unmodulated
conditions. The ratio of driving power of the r-f exciter to carrier power of the modulated
stage should not exceed 1 : 10, since the exciter must maintain a constant r-f voltage on
the grid of the modulated tube. The following formulas show the current, voltage, power
relations, and effect of the variation of the percentage of modulation.
Let Wp — peak instantaneous power output; We = carrier output power; WA. = aver-
age power output, 100 per cent modulation (used in determining heating effect) ; ipc = peak
plate current averaged over an r-f cycle, 100 per cent modulation; ipm = average plate
current, unmodulated; fp = maximum instantaneous plate efficiency averaged over an
r-f cycle, 100 per cent modulation; /c — average plate efficiency, carrier unmodulated;
F = modulation factor = M/IQQ; WLP = plate loss averaged over an audio cycle, 100
per cent modulation; and WLC = average plate loss, carrier unmodulated.
Assume that d-c plate voltage remains constant, and that modulation is effected by
variation of plate current and efficiency. Then:
'
WA = l-5TFc (9)
ipm - 2ipc (10)
/, = fed + F} (11)
WLP - WLC (12)
7-74
VACUUM-TUBE CIRCUIT ELEMENTS
R.F.
16. PLATE MODULATION
The Murtien system of p!at« modulation, devised by Heising, was known as the constant-
current avrtern. Sw Fig. 2. It derived its name from the fact that variation of the
power input to the r-f stage
is obtained by using another
tube or tubes as an ab-
sorber. The current drawn
from the supply source re-
mains constant and shifts
between the absorber and
useful load as the absorber
or modulator impedance is
changed by the a-f voltage
impressed in its grid. Be-
cause of the curvature in the
extremes of the vacuum-tube
Fio. 2,
Amplitude Modulation
eharacwriatias wbea msed as a modulator, the percentage of modulation, where the r-f
«Uff* Mid Biodiiiator are both supplied with the same plate potentials, is limited. To
obtain compel* modulatioa, the d~c voltage impressed on the radio stage is often reduced
by a swrrtw rwafcor. Th« a-f voltage developed by the modulator is transferred, unatten-
»*t«d, t*y n s*iitAbb by-pass e&paofcor «xmn«jeted around the resistor. It is usually pos-
\ complete modulation by reducing the r-f amplifier voltage to 60 or 70 per
; of th« modulator voit-
M^to^itof To modutated ampfifler
Modolatlcm transformer
^-*Mi — designed to carry d-c
W to tfe^T 0X~ compommt of modulated
I 1ft ta^-pOWW ^K amplifier plate current
trftmsmitlers, -ML^
been pr^atly iiaprt>vf?d by
ihf r.La^s C
mtsitAs of & coupling
fornser «od by unnc
of Ki-oiiiilalor tiibe« iri
following the
^«gt may be
with entirely in
Pfatt
which are
limited only by tl** «sa|3^bal-
0! the ¥me$nim tubes
in the roc*iul»tay AXM!
tfier, witlt
high overall eSctenrrj-. Fur
tJ^» eaicuiaUo-n of feuch eir-
anla the rea*ier
to p. 7"- IS.
To modulated ampRfler
fey
the iri<wialai<;vr
Transformer carries
rnodtiiated component
of modulated amplifier
plate current only
t^rminat^d on the
$id^ of tb® co$>-
^ m^f ^®' 3" Modalfttor-amplifier Coujiiog Circuits
aSas«3 »jnp}iS*r 4-c p4*« T^t«§e €^Tid©d 1^- its plate current. It should be noted that,
modulators are iised, the current delivered by the power
la fact, ia the isa«c of tli© pmshpnH modulator, the current
!wy Iwc^* aeeoiid Ittnnoiue. Special attrition must be paid
, «ee Itarai^aaic vokage de-^eloped aoroaa t^ pow^r ripply terminals
COMPARISON OF MODULATION SYSTEMS 7-75
by the modulator current demand will be applied to the modulated amplifier and appear as
distortion in the modulated envelope. Recommended coupling circuits are shown in Fig. 3.
The modulated amplifier is operated class C; however, if distortion is to be minimized,
special considerations are involved. It will be noted that the applied plate supply voltage
to the class C stage has the wave shape of the modulating wave. It follows that, for 100
per cent modulation, the voltage rises to twice the carrier level, and the plate current must
likewise rise to twice its quiescent level. Adequate grid excitation must be provided to
insure this increase in plate current. This is usually achieved by driving the modulated
amplifier somewhat harder than is required to produce rated carrier power at maximum
efficiency. In addition, grid leak bias is used, and since the grid current decreases as the
plate voltage increases (and the plate robs the grid of some of its electrons) the grid bias
falls, the amount of grid driving power falls, and, owing to the combination of decreased
bias and driver regulation, the a-c grid driving voltage increases, thus producing a condi-
tion favorable to a linear relation between modulating plate voltage and r-f output voltage.
The rise in driving voltage required to mininiize distortion is, to some extent, a function
of the design of the tube. Some types of tubes require less increase in drive, as the plate
voltage rises, than is obtained by the combination of grid leak bias and driver regulation.
Lowest distortion will be obtained in these cases if a combination of fixed and grid leak
bias is used. The desired combination may easily be obtained by by-passing part of the
grid leak with a capacitor large enough to retain most of its charge over the lowest a-f
cycle.
Another method of obtaining the necessary variation in drive is to modulate the driver
stage. It is usually not necessary, for optimum results, to use a depth of modulation
greater than 30 or 40 per cent for this stage, when the modulated amplifier is modulated
100 per cent.
Tetrodes and pentodes may be used as modulated amplifiers, If low distortion is re-
quired, it is necessary to modulate the screen-grid voltage.
As in driver modulation, it is usually not necessary to modulate the screen voltage
completely. The modulating voltage may be obtained from the plate circuit of the tube
through a blocking capacitor and dropping resistor or, more conveniently, by a tertiary
winding on the modulation transformer.
Let F = modulation factor; EM — maximum plate voltage averaged over an r-f cycle;
EC — d-c plate voltage; WLP = watts output, complete modulation; WLC = watts out-
put, normal carrier; WM — modulator output power; and Wei — modulated amplifier
input power.
The following formulas show the current voltage relations in a plate-modulated amplifier:
EM = Bed + F} (13)
WLP - 1.5TFLC (14)
,. (15)
The last equation assumes that the modulated amplifier matches the output impedance
of the modulator either directly or through a transformer, since, owing to limitation of
the plate swing of the modulator, incorrect matching may limit the modulation factor,
even though the modulator is potentially capable of producing complete modulation.
17. COMPARISON OF MODULATION SYSTEMS
Any comparison of modulation systems develops into a comparison of means of getting
a specified amount of modulated power into a load, or antenna, under specified conditions
of operation, weight, portability, fidelity, etc. For light-weight, portable transmitters,
grid modulation has some advantage, although it is not capable without feedback of high
fidelity. For most other applications plate modulation is used either directly, in the last
r-f amplifier, or in a stage followed by one or more r-f amplifiers. In the last case, such
amplifiers are usually of the high-efiiciency Doherty type. For transmitters operating in
the standard broadcast band where a transmission is almost always over a single path,
both the "high-level" system of modulation in the last r-f amplifier, and the "low-level"
system using Doherty amplifiers, are satisfactory. However, where multipath transmis-
sion exists, and incidental phase modulation may cause objectionable distortion, high-
level modulation is generally preferred.
FREQUENCY MODULATION. Equation (4), in Article 14 was shown to represent
the modulated r-f current for either the frequency-modulated wave or the phase-modulated
wave. It will be noted, however, that the frequency swing, in frequency modulation,
7-76 VACUUM-TUBE CIRCUIT ELEMENTS
>».*. a*ijM±.m\ £«wk*»s«sjb*'iJ»««r 4m ff'SVTt*!^ oV !
M given by:
» piw» abift IB
Ktv m fi^pwfso* swing in eyelet per second.
I* » moduUti&#«igaa2 frequency in cycles per second.
Method* of placing fwquency aad phase modulation axe discussed more fully in
8-
BIBLIOGRAPHY
CMbv Morny G , Carfter a»4 Sid* Vraqpmqr Bslatioaa with Mdtitone Frequency or Phase Modu-
|«fMHL JICA «»^ V«l. I, lOi-UW <*ahr I««5:
DETECTORS
Bj ycmoa D. Laad«ii
esmootton, ®r 4«tect^m, is the process whereby a wave resulting from modulation
w 10 operated upoa that a wave is obtained having substantially the characteristics of
.
qttftre-v «aa 10 that form 01 detection which depends on the fact that e of
the pow*r &&TWB for & Bma4iii€$ur Hrniit exdted by a modulated wave contains the dif-
lcran«« frvqiWMy between the earner mad oae o! its sidebands, which is the original
Lisear detect!®® is that form c£ detection in which the output voltage under considera-
IMMI « Milwuuilialb* prop^tiiMial to the EBstant&aeoiis peak carrier voltage throughout
tW wwf ml range @l the deteciiiig de\ioe.
m SQUARE-LAW BETECTIOH
Amy d^Tks® having a tKaa-linear cmrent-roltage characteristic will serve as a detector.
droet* feAA ©tri^ra or>nlais a^! tlt^mkmic VM^ium tubes. (See Figs. 1T 2, and
adwla&ed voltage is of the form given in eq, (5), p. 7-72, which, when
a^di*>-fre<4uenc>- terms o! the form
(
SQUARE-LAW DETECTION
7-77
i /
1.5
-^.5
-1.6-ls.2-.8 -.4 0 .4 .8 1^1.6
Impressed VtSUarge
FIG. 1. Static Characteristic of Iron Con-
tact on Ferro-silicon, 25% Fe
1.1
1.0
.9
3-8
g
I'7
1-6
i-s
£
.3
.2
i
i/
\i
f
1
y
/
/
/
/I
,
/
n
^
/
-10123456
Bias Voltage
FIG. 2. Static Characteristic of Diode
rent In MTfflampQres
to 10 G) &> •£
o in o 01 i
^ I
1
I
1
j
1
/
/
/
0
EL
/
/
/
10
/
/
/
0
-r^^
^
—20 -16 -12 -8 -4 0
Bias Voltage
FIG. 3. Static Characteristic of Triode
7-78
VACUUM-TUBE CIRCUIT ELEMENTS
There are two terms present of each original signal frequency, resulting from the beat-
ing of two sidebands against the carrier. From this it is seen that there will not be detec-
tion tinlesa the carrier is preaent, but that the carrier and one sideband are sufficient. If
regard is paid to differences of phase, terras of the same frequency may be added; the
terms preeent and their phase angles are given in Tahle 1.
Table JL Square-law Detection
ExprweBkaa for ita AmBo-lreqaency Current resulting from Square-law Detection of a
Mid Bot& Sid* Baada. ^mEar Terras Appear for each Pair of Audio Components.
T«m*
-f r"
Phase Angle
Triple-primed Values of Resistance, etc.
Apply to Original Modulator at Sending End.
r 4- rp
• — tsn~l -
• + tan-
• — tan'1-
• — fean"1-
r -frp
(2 **» * -f r ft)
. _ taa~^ -
With only <HW midio ecmapoaeat preaent the per cent modulation is 2QOEn/Es = M.
t&e per cent se©c^i<i hmrmoaie present, in terms of the fundamental, is Jkf/4. For
per cent mcwItiifctkMii this system is therefore not satisfactory. When more than
®m signal !rt»qi^ac>' m pneront as modulation on the carrier wave, extraneous frequencies
art produced ec«rr««^>cm4Mi« to UM sum and difference frequencies of all the signal com-
w|«im«4aw ^tortw It ixwr Uurgeiy used only for detection of carriers having small
a and for the reception of single sideband signals. It is the onlv
loam whkfc will wwrk vith theee latter. In detecting single sideband and carrier, second
hmm&mm ol tfe« ai^^ coisapo^tiit^ are not produced, but frequencies corresponding to
tli* «MHi aad dtfftmncwi feetureea tte frecjuencies of the components of the original signal
art prwumt.
BETECTOE CIRCUITS. Any non-linear circuit excited by a voltage
i to that ii^ «t«tk ehatraeteristic over the regkm used is closely a parabola is
m a ^wsai^law <4et««$or. When the vacuum tube is used, detection may
Load
FKL4.
r, Bwtaum Coup4**i to ^HMsccdiog Ampli&er Tube
eiroak®. Figiire 4 shows a circuit which is biased practi-
tstfeas place owing to the curved mutual
LINEAB. DETECTION
7-79
The voltage at any frequency k impressed on the amplifier tube is
ELK
dep
(2)
For high detected voltage the external plate impedance at the carrier frequency (ZB) should
be small, but that at the signal frequencies (zk) should be large. The high audio impedance
is shunted by C, to achieve this result.
Figure 5 shows a circuit in which detection occurs in the grid. The grid and cathode
elements act as a diode detector. The a-f currents, resulting from demodulation, produce
an a-f voltage across the grid leak and so between grid and cathode. This voltage controls
the electron stream so the tube also acts as an amplifier. A high audio impedance and
low radio impedance are necessary so that the grid leak is shunted by a small condenser.
Input
Load
FIG. 5. Grid Current Detector (Z>), Transformer Coupled to Preceding Tube (JL)
This type of detector broadens the tuning of the preceding tuned circuit (owing to the low
impedance of the grid when positive), and overloads badly on strong signals, owing to the
r-f and d-c components of the plate current. It is very sensitive, however.
19. LIKEAR DETECTION
When very large signals are applied across non-linear circuits the power series con-
vergence based on the static characteristics is so slow that the method is not useful. The
equation for the modulated wave can optionally be written in the form (see eq. 6, p. 7-72) :
- 2 2 ^ cos (uKt + 0*) cos (wrf -f- 6,)
(3)
which represents a voltage, of fixed frequency, whose amplitude is slowly varying about a
mean value Es. The sum (S) within the brackets will represent a voltage of the same
wave shape as the original modulating voltage, provided the modulation and transmission
have been distortionless. The instantaneous peak voltage of the carrier current is
-22]T
KES
+
(4)
Rectification diagrams of the detecting device are obtained by plotting the total direct
current in the detector circuit against various steady values of rms (or peak) carrier voltage.
(See Fig. 6.) Then when Em is varied (in accordance with the signal voltage) this current
varies; this detected current is equivalent to a steady direct current, wbose value is de-
termined by the value of direct current which flows when Em = Ett on which is superposed
a varying current which will follow the variations in JEm (and so in the signal voltage) more
or less closely, depending on the linearity of the rectification diagram. Since the periodic-
ity (&>«) of the carrier voltage is not of importance except in fixing the circuit impedances,
the rectification diagrams can be obtained by using any convenient frequency, such as
60 cycles, rather than an actual carrier frequency, provided the circuit impedances are
made equal in the two cases.
YACUUH-TUBE CIRCUIT ELEMENTS
It will b© noticed from tit* rectification diagrams shown in Figs. 7-12 that the incre-
ment in direct current due to a varying grid voltage varies approximately as the square of
the maximum value of this voltage when Em is small (as required by the power series
expansion), but that, as Em increases, the
d-c response varies linearly with Em.
When it does so the distortion introduced
in detection will be small.
As an illustration, consider the plate-
current detector shown in Fig. 4. Currents
of radio frequency are by-passed by C,;
hence the only current which flows through
r when Em is steady is a direct current.
If the value of this current were varied in
accordance with the signal voltage, the
varying voltage impressed on the grid of
the succeeding amplifier tube would be
simply the signal voltage. If the variation
of direct current against Em were given by
the curve of Fig. 6 and the average value
of Em were equal to OA, then the varia-
tktn 0f rumemt would b© exactly proportional to the signal voltage, even for 100 per cent
mGdulotum, provided Em < OB. This njeans tiiat there would be no distortion introduced
by the defector.
Although ao drrk© avmHa&kf at present has exactly the characteristic of Fig. 6, certain
eiyetale appnminiAfe© it, aud the vacuum tube can be made to approach it by a proper
<u
I
C
Fw
x
/
Et
-*.<
«»«..,
XI
r-
X
/f
> A B
, C Ideal Defcwtor Ch»r»rleii8tk (Bectifica-
A 4fio4»
*ctifi«*tian Da«f»m for E^xfe Detector
. f%nr« 7 sfeows a set of curves f or a diode f torn
<ij»&mm fer aaay load nssfeiaaee can be ofc^ained; the diagram for
m rnmem m F%. 8, wfekii «o«iM also have been obtained expeiimentallv
t h* aeftrebt apt^^di to liaaar &s*e«$i©B of anj- kaown detector.
LINEAR DETECTION
7-81
When the characteristic is not a straight line, a Taylor's series expansion can be used
in terms of epa and the change (em) hi Em:
dip
dip
(5)
and em, tp is the plate-current ordinate of
80
50
s
40
230
20
10
where ipc is the current due to the variations ej
the rectification diagram, and epa is the
plate potential due to ipa and em. The
reciprocal of dip/dep is the analog of the
plate resistance used in Section 5, and
has been named the detection plate resist-
ance. The derivative dip/dem is the slope
of the rectification curve — it is analogous
to the mutual conductance of a triode and
is called, the detection mutual conductance
or the transrectification factor.
All the calculations given for class A
amplifiers now may be utilized in the
detector circuit, including calculations of
distortion, detection efficiency, etc.
LINEAR DETECTORS. As stated
above, the diode gives the nearest ap-
proach to linear detection known today.
It has the objection of putting a fairly
small resistance in parallel with a tuned
circuit and so considerably broadening
the tuning. When a diode is used the
applied r-f voltage should be made as high
as the tube can stand and a load resistance
selected to give minimum distortion.
The triode is not as distortionless as
the diode but sometimes fits in better
with the circuit requirements. Rectifica-
tion diagrams of a triode alone and with
load are given in Figs. 9 and 10. In gen-
eral, the plate voltage should be as high as possible, limited only by the supply available
or the limits of the tube itself (flashover or heating).
When the plate voltage has been determuied, rectification diagrams of the tube alone at
various grid biases are obtained. If it is desirable, as is usual, to use the tube with carrier
voltages which are 100 per cent modulated, the plate current should not reduce to zero for
any finite value of Em, or part of the modulation will produce no effect. In other words,
the tube should not be biased below cutoff. The best results will be obtained if the tube
is biased at, or slightly above, cutoff (on
the static characteristic); this condition
will be indicated on the rectification dia-
gram by a small plate current for Em = 0.
For the tube of Fig. 9 the grid voltage is
thus determined as either —1.5 or —3.0
volts.
To determine the proper load resist-
ance, rectification diagrams of the tube
with different loads (see Fig. 10) are ob-
tained. If Em is varied over a straight
portion of one of these curves, distortion-
free detection will result; if the variation
is over a curved portion the distortion may
0 5 10 15 20 25 30
RMS Signal Input Voltage
FIG. 8. Load Rectification Diagram for Diode
Using 500,000-ohm Load
6 8 10 12
Eja. (S-M-S.) in Volts
FIG. 9. Rectification Diagrams of Triode (Alone).
All data were taken with 6Q-cycle impressed voltage.
be calculated as for an amplifier. (See
p. 7-07.) For the tube used here a load
impedance of 30,000 ohms would cause
the tube to introduce a very low percentage of distortion for a carrier having an average
rms value of 6.25 volts, and 100 per cent modulated. The difference between curves C
and E illustrates the gain in efficiency, but increased distortion, obtained by by-passing
the load resistance.
When the triode is used as a detector with large signal voltages of high percentage of
modulation, operation with niinimum distortion is always accompanied by a positive grid
7-S2
VACi'UM-TUBB CIRCUIT ELEMENTS
fwiniE aad *o a flow o( grid current. This causes a low input impedance and so decreases
the **<ertivi?y of the tuned circuit just preceding the detector.
Th* w of * tetrode <**e Fig. ID makes it possible to obtain rectification diagrams
wiirh r*a*h ^turation for negative v&Jue® of control grid voltage, so giving straighter
operating run** without lowering the input impedance of the tube. The same method of
foikwed, the only additiaaal factor being the proper voltage to use for the
_ _ ^ screen grid. The method employed in se-
-jUa
.gfof ...
lecting the screen-grid voltage depends to a
large extent upon the type of plate load.
In general, a higher screen-grid voltage gives
a better rectification diagram (straighter
and steeper). However, when there is a
large d-c resistance in the plate circuit, the
plate voltage falls considerably for large
signal voltages, so that, if the screen-grid
voltage is comparable with the plate volt-
age, electrons will land on the screen grid
rather than on the plate.
When reactance coupling is used the
screen-grid voltage should be the maximum
consistent with the plate voltage. For this
type oJ coupling the d-c resistance of the
detector plate load is small enough so that
large carrier voltages will not cause sufficient
drop for tht plate voltage to beeome comparable to the screen-grid voltage. Therefore,
there w ao Beeeerifcy ©£ keepsf Uw acne^n voltage low to preve&t saturation (on the
diagram), &nd il&e gala in mutual conductance with high screen voltage raises
,uvh> md maximum cmtpm as well as decreases the curvature of the rectification
is iaa©d the- selection of the optimum screen-grid voltage is
> probbm la to select a value of screen-grid voltage that will
output at the normal values of input and yet not cause over-
of input voltage. Two rectification diagrams for different
a taigti resistance bad are shown in Fig. 12. The curve for
£
lilt
WVra rewtiaiew
£wn»iimfcl®
for the larger
« 7S Tc4t« u
tub© ovwrfewli for
- — 12. Load HjsctlficatioD Diagrams of a
Tetrode, Slewing t^e Elect of Screen Grid
Voltage oe Satomtioft. (Resistance load.)
« 40 volts for inputs up to a point A, but the
•*« -4. It is thtis necessary to know the maximum
os the detector, and the screen-grid voltage which
BIBLIOGRAPHY
) Voha^a-^PU^ R«ctifimtioa ni^ the ^^-vscniim TAxte.
VACUUM-TUBE OSCILLATORS 7-83
OSCILLATORS
By Carl C. Chambers
An oscillator is a non-rotating device for producing alternating current, the output
frequency of which is determined by the characteristics of the device. Oscillators can
be conveniently divided into three classifications: (1) vacuum-tube oscillators, (2) elec-
tromechanically controlled oscillators, and (3) spark-gap oscillators.
20. VACUUM-TUBE OSCILLATORS
The most generally used oscillator in the field of communication engineering is the
vacuum-tube oscillator. Since a vacuum tube can act as an amplifier of power, it can
act as an oscillator. The power needed in the grid circuit can be supplied by the plate
circuit. A vacuum-tube oscillator circuit acts as a power converter, changing d-c power
into a-c power, having a frequency determined by the parameters of the circuit. The
efficiency of vacuum-tube oscillators can be above 90 per cent, although for many
purposes they operate at low efficiency. Vacuum tubes are constructed to dissipate as
high as 125,000 watts, the power output of oscillators using such tubes being much
greater.
SIMPLE OSCILLATOR CIRCUITS. In ordinary vacuum-tube oscillators, power is
fed into the grid circuit from the plate circuit by means of either electrostatic or electro-
magnetic coupling between these circuits. When sufficient voltage of proper phase is
introduced into the grid circuit, the a-c component of the plate current will persist, or, in
other words, the circuit wiU oscillate.
Many oscillator circuits have been devised, several of which are shown in Fig. 1. In
each of these circuits, the oscillatory circuit is the mesh containing L and C, In the
Hartley circuit, the inductance L is tapped (not necessarily at the center) ; in the Colpitts
circuit, the capacitance C is the series capacitance of Ci and C%. The tuned-plate tuned-
grid oscillator has two separate oscillatory circuits, one in the plate circuit and one in the
grid circuit, both tuned to approximately the same frequency. In each of these oscillators
the load is coupled to the oscillatory circuit. This coupling is usually but not always in-
ductive coupling.
The voltage introduced into the grid circuit due to the plate current, in (a) and (6), is the
drop across part of the oscillatory circuit. In (c), (e), and (/), it is the voltage across one
winding of the transformer, one winding of which is the inductance, I/, of the oscillatory
circuit. And in (d) it is the voltage drop across the grid oscillatory circuit due to the
current through it and the grid to plate capacitance. The peak value of this feedback
voltage in each case must be great enough to cause oscillation to persist. For stable
operation, it should be roughly two and one-half to three and one-half times the d-c grid
voltage necessary to bias the tube to plate current cutoff at the operating d-c plate poten-
tial.
The capacitances, C.B, are by-pass condensers, and the inductances, LB-, are choke
coils arranged to prevent the alternating current from passing through the d-c supply
source, SB, or through the biasing resistor or grid leak, TB- The grid voltage in most
oscillators goes positive for part of the cycle. Thus the grid bias voltage is conveniently
obtained by means of a grid leak and condenser. This method of biasing the oscillator
tube tends to self-adjust the grid bias to permit operation over a wide range of values of
the feedback voltage, since with greater excitation the grid tends to go more positive and
consequently the grid bias becomes greater, resulting in essentially the same plate-current
flow. Some oscillators have a comparatively small external grid bias (or self-bias by
means of a cathode resistor) in addition to the grid leak. This externally supplied bias
is a safety device to prevent too much plate current from flowing if the oscillations should
cease for any reason,
WOK-LINEAR THEORY OF OSCILLATIONS. "'The complete solution of even the
simplest oscillator circuits is extremely complex. However, van der Pol, by means of very
radical assumptions, has obtained the solution of several oscillator circuits. One of these
solutions is for the circuit shown in Fig. I/, The following assumptions are made con-
cerning the circuit: (1) that the grid bias voltage is obtained by means of an external
electromotive force; (2) that no current flows in the grid circuit; (3) that the capacitances
CB are so large that their a-c impedance is zero; and (4) that p, the amplification factor,
is constant. These approximations make the solution useful only from a qualitative stand-
point.
7-84
VACUUM-TUBE CIECUIT ELEMENTS
Thf OMMMiy condition for omllation to persist is found to be that a, the damping
eooauat of the rirruit taken as a whole, is negative. To a rough approximation the ampli-
ttxfo 01 tin* oftcillation sa proportional to the square root of the ratio of a to the coefficient
of th* rob* t*rm in the power series expansion of the characteristic of the vacuum tube.
Tb» WTO form of th® o*ciU»tion is dependent upon €, the product of a and LC. The
f UMI circuit to semral values oi « as calculated on the differential analyzer at
ijtj
/-i
n
^:C
•t
B
'h
1. C<mvim®@&»l O^fllatw Circuits
Moort Sebool c^ Electric*! En^iuwring are stown in Fig. 2. For smaH values of e,
tht
ti*l!y mfii«sidaat the frequency being given by
For
f t, the o»cifa^s9ti« d@p^i ra<H«aUy from sme waves. This form of oscillation
«*IM rdi!t*®feia ««aU«ltMi. It oerurs ia the multivibrator, the human heart, the
ie ram, etc- Van der Pol pws the period f or « i?> 1 as roughly equal to 2e.
GOWDITIOirS FOR S!I#~0SCttLATIOlf. For smaM amplitudes of oscillation, the
B$»4iia«fcr rm®i&$a&&m ©f UMI |slml«f SMK! grid circuits can be approximated by linear resist-
aaa^e^ Tfe® ©e»ditkm for ilsw© §maH o*ciU»tktti8 t© build up is that the damping constant
& Fw$*tive. Tlas u th« fsmwlitw^ for unatabb systems in traa^ent circmt theory. How-
««». as th* ©neiaatti^M meimw in amplitude, the linear circuit theory fails.
U»*Ptip» h*^ ^@wa that. um«irr ^aady-«tai« operatioii for any freqijency component
«f A® funw&l* & m^*toe«r r®^^a»cft ew be replaced by an e*j*iivaieBt impedance which
I^IF a^wosimattd by a pure nssistanee. When the circuit oscillates
. ti» HMMAMOMHUI ir««jntacy ot oi^iat^i has a coolant amplitude so that the
VACUUM-TUBE OSCILLATORS
7-85
plate to filament circuit in the tube can be replaced by such an effective resistance. In
order for steady-state currents of a given frequency to flow in a circuit containing no emf
of that frequency, the determinant of the coefficients of the currents in the mesh equations
must be zero. An oscillator must satisfy such a condition. The approximate resulting
conditions are noted for most of the circuits in Fig. 1. The value of the effective plate
resistance, rp ,for any amplitude is given approximately by the inverse slope of the secanc
joining the limiting points of operation on the plate characteristic of the tube. By the '
reverse calculation the magnitude of oscillation for any given circuit can be predicted.
6=0.1
r\
^-v^
/~\
/
\ /
\
X
_/
\y
\ /
\ ,
^
M
10
4-
0
I
_/~\
/ \
I
\ /!
V
j
\ I
\ /
i
^
v
20
25
10
15
20
/ \
e=i.o/
\
/ \
y\
/ ^
, /
\
/ \
\
/
A /
\ y
r v
\
y
\/
/
3 5 10 ~ 15 w 20 2
-ft
/N
/ ^e=2.o
! X
•
/ \
/
\
1 \
\
/
I /
\
/
\ i/
\/
\
1
/
0 5 10 15 20 2!
-H
PIG. 2. Solutions of van der Pol's Equation for the Non-linear Theory of Oscillations:
(fl ~ «<1 ~ *2> | + u - °)
CURRENT AND VOLTAGE RELATIONS IN SIMPLE OSCILLATOR CIRCUITS. ,
As stated at the beginning of this chapter, the vacuum-tube oscillator is simply an ampli-
fier arranged so that the power needed in the grid circuit is supplied by the plate circuit.
Ordinarily, the amplifier so arranged belongs to that group known as class C amplifiers.
The current and voltage relations of a typical oscillator are shown in Fig. 3 for one
complete cycle. The plate current flows during the portion of the cycle when the instan-
taneous plate voltage is least so that, since the energy- dissipated at the plate of the vac-
uum tube is the integral of the instantaneous plate voltage times the instantaneous plate
current, the tube plate loss is least when the current flows for as small a portion of the cycle
as possible. When plate current flows, the grid voltage is positive with respect to the grid
bias necessary for plate-current cutoff. Thus the duration of plate current decreases and
consequently the plate efficiency increases with simultaneous increases in the grid bias
and the a-c grid voltage. However, increasing the grid voltages in this way increases the
losses in the grid circuit. The a-c grid voltage usually has a peak value of two and one-
half to three and one-half times the grid bias necessary for plate current cutoff at the d-c
plate voltage.
Since plate current flows only during minimum instantaneous plate voltage, the mini-
mum plate voltage is of major importance. The impedance of the oscillatory circuit at
resonance is adjusted so that, for the normal power output, the peak a-c voltage across it
is slightly smaller than the applied d-c plate voltage. Therefore, the plate voltage causing
current to flow is small compared with the d-c plate voltage, since it is essentially the d-c
plate voltage minus the peak a-c voltage across the oscillatory circuit. Thus the a-c and
d-c voltages remain practically equal as the d-c voltage is varied. It is this equality
between the d-c and a-c voltages that makes the plate modulation of oscillators and class
C amplifiers so nearly linear.
In ordinary triodes, the maximum plate current flows for a positive value of the grid
voltage somewhat less than the rrdninmm instantaneous plate voltage. In most oscillators
at full load, the relation between the plate voltage and the grid voltage is such that the
7-S6
VACUUM-TUBE CIECtJIT ELEMENTS
YalW Ol in« IP*** i«aut MS ueoi. M^W*****"^^ «j — _ -i*
Tolt*«e is about 0.8 of the minimum instantaneous plate voltage, in small
Zero Time
CWTWB* Km! Vota* EelstaQiaa of a Representative OseSJator
> dficieacy is so* Tital the value ©I tl*e grid leak can vary over wide limits; a value
taw from & few thousand ©hms to a megohm may be determined by trial and error
until the oB«aEator operate® satisfactorily.
Sou»tii3i©8 wl»n the time e<»^«at ®f the grid leak sod condenser is high and when
Oit rati© of the »HD pU^a voatape to th« a-c g?id voltage is low, "blocking" will take place.
"" " ! *& a r»Iax»tkBa oscallatioa and is due to tfee grid being at a higher potential than
» a© that tbe seoo^ary ^a»k»i I ttsm Hi© grid causes the grid leak and condenser
p a iugh b$&i wfekli stop* tii« o®cilliiti<» imOi the charge leaks off the condenser,
at whieh «inw «^il»ti«^i y^m atari «ad the cy^» it^>eats itself . It can be corrected by
i&mttiixte th* f»lk> ol ta* *-e plate voita^ to tfee M grid voltage.
0BCP<lnJt.TOaTY CIEC0IT DESIGN. The heart <^ any sinusoidal oscillator is the
„ ol aa inductance and a capacitance oonnected in series.
h ^ai mspplaed to this circuit from & d-c source by a^ans of a vaeuum tube, and
11 m i*ken «nw^r Inoaa it by co^plkig tlae load to it in otae of varioiis ways. The
swaH**- to A»t ol the Sywfeeel im a nsdproci^iiig steam
VACUUM-TUBE OSCILLATORS
7-87
The oscillatory circuit must store the energy used by the load long enough so that it can
supply the load continuously even though it receives energy only during a small portion
of the cycle. It has been found empirically that in order to do this job effectively, i.e.,
to give a good wave form, the ratio of the peak energy stored per cycle must be at least
twice the energy fed into the load per cycle. From ordinary circuit theory it is known
that a load resistance paralleling a tuned circuit, or coupled to a tuned circuit, can be
replaced approximately by a resistance in series with the tuned mesh. When this is done
the ratio of the peak stored energy to the energy dissipated per cycle is
VI
r-r
(1)
where V is the rms voltage across the capacitance, C, and across the inductance, L; I is
the rms current through the inductance and capacitance; r(= L/rzC, where TL is the
shunting resistance load) is the effective series resistance of the circuit, assumed to be
small compared with 2x times the frequency, /, times L. Thus if the ratio is to be greater
than 2, 27r/L/r(=: Q) must be greater than 4x. This Q refers to the inductor together
with the equivalent resistance due to the load.
On the other hand, if the ratio L/r(— TL€ = TL/^fiL) is made too large the resonant
resistance of the circuit will be too high to obtain a satisfactory power output. It is
therefore necessary to compromise between power output and wave form. It is in gen-
eral good practice to make the ratio of the stored power to the power output about 2,
i.e., to make Q = 4x. L and C are then given in terms of the power, the frequency, and
the voltage (essentially the d-c plate voltage) as
L
L
(2)
c=w (3)
These formulas are not meant to be critical. If good wave form is more important, use
a value of P in these formulas greater than the actual power; if power output is more
important use a value of P less than the actual power. This principle is frequently stated
by saying that the wave form is improved by decreasing the L to C ratio of a tuned circuit.
These circuit considerations apply equally well to the tuned circuit of a class C amplifier.
CONSTANT-FREQUENCY OSCILLATORS. Using the equivalent impedance dis-
cussed under Conditions for Self-oscillation, above, (a) and (6) of Fig. 1 are special cases
of the equivalent circuit shown in Fig. 4. The ordinary mesh equations for this circuit are
- Ipte 4- 2m) + lite 4- *2 4- Z* + 2*m) - /ife + *») = 0 (46)
• 2«) 4- Ig(zg 4- 22 4 z*) =0 (4c)
Most of these impedances are functions of the frequency. And, since the condition that
any of these currents can be other than zero is that the determinant of the coefficients of
the Ps is zero, the frequency of oscillation is the
frequency which will make that determinant zero.
Thus the frequency depends not only upon the
parameters of the oscillatory circuit but also on the
other parameters of the circuit. In order that the
frequency shall remain, constant, all these param-
eters must in general remain constant.
To keep the inductances, capacitances, and re-
sistances external to the tube constant is a prob-
lem in the design and temperature control of those
parts. On the other hand, regardless of the de-
sign, the effective impedance of the tube itself
changes with use and supply voltages. Several
methods have been devised to maintain essen-
tially constant supply voltages, and seasoned tubes
tend to reduce the changes in the tubes themselves.
However, by adjusting the other circuit parameters the dependence of the frequency on
the tube impedances can be minimized.
The most common method is simply to increase the sharpness of the oscillatory circuit,
that is, decrease the decrement of the circuit. This is carried to the extreme by the use
of mechanical resonators such as the quartz crystal and the magnetostriction rod.
FIG. 4. The Equivalent Circuit of Most
of the Circuits of Fig. 1
7-«8
VACUUM-TUBE CIRCTJIT ELEMENTS
Uewrfyn baa d*m>ver*d that, fey proper adjustment of the impedances Z< and Z& it
hb tn the limiting caae of no harmonic currents in the tube to ehmmate the depend-
of the frequency of oscillation on the tube impedances. Although this limiting case
new re&cimi the w of tlie« impedance® tends to stabilize the frequency. In addi-
tion it is sometimes possible to change the frequency by a,
simple change in the parameters of the oscillatory circuit
witbowt disrupting this independence of the frequency on the
tube impedances. A circuit derived from the Colpitts cir-
cuit for this purpose is shown in Fig. 5, where 1/4 — LzCi/Cz.
Ttiu« the frequency can be adjusted by changing Ci and Cg
proportionally without changing the calculated value of L±.
THE HARMONIC CONTENT OF OSCILLATORS.
From the non-linear theory of oscillators (see article 20) it
is known that an oscillator is stable only if it is non-linear.
Thus an oscillator always produces harmonics in its output.
Tbe percentage of the harmonics becomes small when € be-
comes small, that is, when the feedback from the plate
to the grid dretilt is small. A circuit applicable at low frequencies in which the
f«dhaek can be controlled is shown in Fig. 6. The variable resistance r controls the
amount of ftfxilmek. Tfam circuit not only has a controlled harmonic content, but it also
is wry *tmU« with frequency. It is exeeUeat for a laboratory oscillator where r can always
fee mdiust^d to emnpenMte for changes in tbe tube characteristic.
In large oscillators aad class C arapMSfcrs a aeries tuned circuit is sometimes connected
m aeriee with tfa« plate eimiit to offer a high impedance to the harmonics. Such a tuned
euwutt, m additwa to decr^ast&f the Ifcrnrsaoaie content to a marked extent, increases the
Fi* 5, A r<*w«iiit
qwwry C»mnt Pwjwdi from
a C«jfft«
SEPARATELY EXCITED OSCILLATORS, Separately excited oscillators are a special
C mmpJi^ers, The volt&gp© an&d current relations of the true oscillator are
of a properly operated daas C amplifier. If, however, the frequency of
vt»K«0» differs from timt at whicfe tbe tube would oscillate, the plate-current
wmv® form n M34 aymtiMtnail about the icro ordinate shown in Fig. 3. Increasing the
diMormaMttry <rf tliia wmv© by vmryiag the capacitanae of the oscillatory circuit increases
ttet awrmfe or d-r euirrt^t. Thus tlie freqtiency of the c^cillatory circuit is adjusted in
ihitt t>"pe of da^ C ampliiers until the d-c ctirrent is a minimum.
Most of the theory wad empirical relatkus given for oscillators can be applied to class C
I — <wWwv — j
OF OSCILLATORS. When two oscillators oscillating at
freqwiaesfcs are loosely coupled together, they mutually distort the voltage
acTcw their oscillatory circuits. Tfeis distortion in turn distorts the current and
discussed above. This distortion causes a magnified distortion of the
plat* etsrrtat sine* rum a small per cent change in the oscillatory circuit voltage has a
great effect o® th* minimum plate voltage. This change
i an addition*] change in the voltage
; the cwetll&tecy cirt-uit drop directly ami indi-
? throiigh th® «$iaii||e m Thus the volt-
aic due to lib© one oscillator causes & magnifiecl change in
the other oecaUator. Thin distortion tends to shifi the
phaa«» ©f the pl»fce wit*«© with iwpeet to the grid voltage,
When th» ^iase ehtft exc^wls tfee limit alkmmHe for
• omUatiofj, the o»«allator jump* into oscillation at
h of the other oa^cilliitcM1.
Hie ndnerabiUty ^ «® osaflator to symtferwbatioa increases with the i to C ratio
of the weiaatory circuit. T&m wfe«m tim oeeiliators are to oscillate independently even
t thwe ia a «miptint; betwwa them, the L to C ratk> sbotild be made as small as is
; with ' " " "~~ "
FIG. 6. An Oscillator for Low
Harmonic Distortion
• to owHist© at tiie fre^iicy of a master oscillator without
__ .„.._„„ „ _^ taaeter oscffla^r, it is a«f?es^ury that the coupling between
the aecOteum be uaidirwkioMl. Tlmt b, the rmetion of tfee secondary oscillator on the
HM fee iMfliKibie. ^^ coupling caa be obtained % means of the
CaiiUK srwral ^icli amplifiers, each fed by the master oscillator, the
F aenwmj oscillators ran b@ eimtrolW by the freQtiency of the master o&eilla-
«•» !>• «3f»«fe3®ib«»d at A subharmonie ol an introduced voltage. The
m$m with a pifclj»roHmk <^ the introduced voltages m no* as great as
I. anal ©eaaimtiowi so obtained are relatively unstable.
VACUUM-TUBE OSCILLATORS 7-89
BEAT FREQUENCY OSCILLATORS. In order to satisfy the conditions for stable
oscillation many of the circuit parameters must be changed when the frequency is changed
over a relatively large range. For continuously variable frequency over a wide range,
especially over the audio range, it is difficult to make the necessary changes in these
parameters. For the same absolute change in frequency beginning at some high fre-
quency, only one parameter, usually the capacitance, need be changed. If the outputs of
two oscillators of relatively high frequency are introduced into a square-law detector, and
if all the high frequencies are filtered out, only the difference frequency is left. Then as
the frequency of one of these oscillators is varied from the frequency of the other to that
frequency plus 10,000 cycles, the output of the detector varies in frequency from 0 to
10,000 cycles. Such an arrangement is called a beat frequency oscillator and when prop-
erly built is an excellent laboratory instrument.
Care must be taken to insure that the intercoupling between the oscillators is so small
that there is no tendency for them to synchronize, since this will introduce distortion in
the output of the detector due to the distortion in the oscillators themselves. This can
be prevented by mechanical or electromagnetic segregation and balanced bridge circuit
feed to the detector, or by amplifiers between the oscillators and the detector.
DYNATRON OSCILLATORS. If, in a vacuum tube, the grid voltage is made more
positive than the plate voltage, some of the electrons which attain a high velocity between
the cathode and the grid pass through the grid openings, their velocity carrying them on
to the plate. These electrons may then knock electrons from the plate. This process is
called secondary emission. In some cases secondary emission may exist to such an extent
that an increase in plate voltage actually causes a decrease in
plate current. Thus, when a tube is operated under these con-
ditions, the a-c plate resistance is negative. A tube operat-
ing in this way is called a dynatron.
An oscillatory circuit connected across this negative resist-
ance (Fig. 7) will oscillate provided the absolute value of the
negative resistance is less than L/rC. Owing to the small F " Th C* *t f
range of plate voltage over which the resistance is negative, IG" Dynatron Oscillator0
these oscillators have not been made to give very large power.
OSCILLATORS AT HIGH FREQUENCIES. At high frequencies, of the order of 50
Me, in the case of ordinary receiver tubes, where the time of transit of the electrons
between the tube electrodes becomes an appreciable part of the period of the wave, the
grid impedance can no longer be considered an open circuit or even a pure capacitor.
Under these conditions, the displacement currents arising from the motion of the electrons
in the space between the grid and the other electrodes causes a true dissipation of energy
in the grid circuit within the tube and a direct conductive coupling to other electrodes.
This causes a grid-circuit loading of the tank circuit, decreasing the oscillator efficiency.
As the transit-time effect first becomes important, the resistance of the grid due to this
decreases approximately as the square of the frequency. Consequently, as the frequency
of oscillation is increased through this frequency range, the efficiency decreases rapidly to
the point where oscillations can no longer be sustained, even though no external load is
coupled to the tank circuit. Decreasing the dimensions and spacing of the electrodes in-
creases the frequency at which transit-time effects become important but correspondingly
decreases the power-dissipating capacity of the tube.
At high frequencies, another effect becomes important. The leads within the tubes and
the socket are found to have an appreciable impedance. Such impedances must, of course,
be considered part of the circuit when that circuit is designed. In many tube types the
impedances associated with the leads are so prominent at high frequencies that the highest
frequency at which these tubes will oscillate is limited by this consideration rather than
by the transit-time effect discussed above.
Since the efficiency of ordinary oscillatory circuits decreases as the frequency for which
these circuits are designed increases, it is common to replace coil and condenser type tank
circuits by resonant concentric lines. Thus in the tuned-plate tuned-grid oscillator circuit
of Fig. l<f, two concentric lines are used, one replacing the tuned-plate circuit and one
replacing the tuned-grid circuit. The adjustment of the resonant frequency is accom-
plished by movable short-circuiting plugs ha the lines. Various configurations of the con-
centric lines can be readily adapted to this circuit.
To accomplish the combination of improvements to overcome the adverse effects of
transit time and lead impedance, and to adapt the tube for use with concentric line circuit
elements, the so-called "lighthouse" tube was developed (see Section 4). Using such
tubes, triode oscillators have been operated above 3000 Me.
THE MULTIVIBRATOR. For large values of e the non-linear theory of vacuum-
tube oscillators discussed above indicates that voltages having a discontinuous wave form
7-90
VACUUM-TUBE CIECUIT ELEMENTS
-JH
li
resistance-capacitance coupled amplifiers
connected as shown in Fig. 8, so that the
output of the second is fed into the in-
put of the first. Under these conditions
the phase of the output voltage is such
as to aid the grid of the input tube. The
period of the oscillation is given roughly
by rgiCi -h J-tfCa. Using ordinary tubes
these oscillators can be made to operate
at frequencies up to 1,000,000 cycles.
fm, 8. Tls*» UMa3 Muhfribtaior Circuit
BISTORTIOHLBSS OSCILLATORS. As indicated under Non-linear Theory of
OMittaton p. 7-83, it is geftfrrally necessary for a stable oscillator to operate m such a
way that MI increase in grid-volume amplitude would cause an increase in limiting-type
difltoruoa so that the voltage developed in the plate circuit produces too small a voltage
is the grid circuit to maintain that voltage in the plate circuit. And similarly a decrease
in grid-voltage amplitude would produce such a relatively increased voltage in the plate
circuit that a larger voltage wowkJ be produced in the grid circuit, tending to return the
gnd-vohage ampKtwle U> its original value. Under these conditions, the stable grid-
votage ampittide ia mtfa thai the voltage developed in tbe plate circuit is just sufficient
to maiaiA^ that stable grid voltage ia the grid eircuit. In other words, the voltage gain
at tla* oseaBbtimg fwqtteney must cleerease as the amplitude increases and must increase
m Us® am$$£fc®&n &&&&*%&&, 1^0 ^««*er the mmguitade of this dependence of gain upon
amptifcacfe, %^ «r«a^r the Natality <^ tte oscillator. In the ordinary oscillator, where
thie <l&pTOd«»i» ol gaia upon amplitude is iMScomplislied through amplitude limitmg, the
p^^isr th« dfcpefsd®&**t tl^ greater tli© diBfcortkxu Consequently, it is generally true
that am foorwawi in atability c^ an o®ci!lat#r is accompanied by an increase in distortion.
IB m& escsEator wter® ^e paa of the amplifier part of the circuit is controlled by the
mwr«®t affitplilwie, »fseriigt«l ovw one or more cycles, rather than by the relatively in-
•4«atAi3&©ii8 limiting actioia ol ib© ordinary oscillator it is possible to operate the amplifier
in tliat part c^ il* Aar»«teri«ue where dk40rtk)i3 is negiigiWie. One such oscillator is the
resa^^c^-e&pacitAziee oscillator,
»-C OSCBXATOIL Tlie reneta«Me-eapa«itanee tuned oscillator is shown in Fig. 9.
Tfee> bride* ««»*• at tlie left of the circuit is a somewhat unbalanced Wien bridge at the
iiaeillataic ff^faeocy, 5/a ar v rir^7jCj, Tbe wabalaace is such that, were rj to be somewhat
, the bridfe would be balanced. Actually, r0 and r& are so diosen that the un-
foh&ge wMdb i* iiitrcxliieed in tb& grid carcint of the first amplifier tube is just
wfeen ampttied to ppxtiKws the requked bridga suppy voltage between A and B
to Bs&intAija llutt .^j^g^**-
t»d> el tin tsal»a«e vt^lta^s. i w*** j^-
If ti%@ gjiiii o^ tJbe airsplififfif
from its
Tbua such am osciliaior is amplitude stable at the frequency
If rjCi » rtf* the maximuni positive balance voltage
at Mi bwniMMBy. Tfeer^we» this oscalUtor operates staUy at only 01^ fre-
Tba fijiia* ex>iiut>l b aLverac*d ov»?r several cycles owing to the thermal lag of
.tAsafe cha<R«e <rf HM laxrip. By iiiefif is of g&iiged condensers lor C2 and C±1 the f re-
ELECTROMECHANICAL OSCILLATORS 7-91
quency of such an oscillator can be conveniently varied. Oscillators of this type can be
designed for frequencies well below the audible limit to several hundred kilocycles.
OSCILLATIONS OF GAS-FILLED TUBES. The gas-filled tube characteristic differs
from the vacuum tube in one outstanding particular. The plate resistance varies from a
very high value to a very low value almost discontinuously. Such a characteristic does
not lend itself to the production of sinusoidal oscillations. However, it is highly advan-
tageous for the production of almost discontinuous wave forms, the most important of
which is the so-called sawtooth wave used for linear scanning hi cathode-ray oscillographs.
The circuit of such an oscillator is shown in, Fig. 10a. The condenser C is charged
through the resistance r until the voltage across C is equal to the critical starting voltage
of the plate circuit, the volt- _
age at which the resistance | \^f\ ^ \ Rate voltage
suddenly decreases to a low
value. The condenser is then
discharged until the voltage
across it equals the critical uH|i|l| M|l|l|l| Cb)
stopping voltage, the voltage (aj
at wMch the plate resistance FIQ ^ A Rela^ation 0sciUator, Using a Gaseous Tube, and Its
returns to its high value Voltage Wave Form
again. This stopping voltage
is always less than the starting voltage. The cycle then repeats itself as shown in Fig.
106- These oscillators can be operated fairly satisfactorily up to 15,000 cycles, being
limited by the ionization and deionization time of the gas. Above this value multivibra-
tors must be used for linear sweep circuits.
These oscillators are easily synchronized with an external frequency by introducing a
voltage at that frequency in the grid circuit as shown in the figure. As with vacuum-tube
oscillators, these oscillators can be synchronized at a subharmonic of the synchronizing
frequency.
BARKHAUSEN OSCILLATORS. In 1920 Barkhausen and Kurz discovered that,
using certain tubes, oscillations a few centimeters in wavelength were produced when the
grid supply voltage was highly positive and the plate was at or near the cathode potential
Several theories of the operation of tubes under these conditions have been proposed but
none agrees entirely with the experimental results. Practically all tubes which will oscil-
late under these conditions consist of cylindrical and coaxial cathodes, grids, and plates.
Some investigators have succeeded in getting oscillations from other geometrical con-
figurations, notably planes instead of cylinders.
Qualitatively, the explanation given is that electrons rapidly accelerated by means of
the high grid potential pass through the grid as a result of their momentum and are turned
back toward the grid, owing to its high potential, before they reach the plate. This causes
each electron to set up a displacement current between the grid and the plate. A chaotic
distribution of the phases of the oscillations of these elec-
_ utpuf £rons can De shown to be an unstable distribution. How-
ever, when these electrons oscillate in clouds the operation
is stable so that the resultant current is not zero.
The customary circuit for these oscillators is shown in
^8* H* ^ke power of the oscillations has been observed
as k*gk as ^ watts' *h.e wavelengths go to 6 cm, and the
-D rr efficiencies are from a fraction of 1 per cent to 7 per cent.
mSoi • ^ The lowest efficiency and the lowest power usually occur at
the shortest wavelengths.
OTHER SPECIAL OSCILLATORS. Other forms of oscillators use resonant cavities
for the oscillating circuit element. These are treated in Section 4, article 8, on magne-
trons, and article 22 of this section on cavity resonators.
21. ELECTROMECHANICAL OSCILLATORS
The frequency stability of mechanical vibrating systems is in general better than the
frequency stability of electrical oscillatory circuits. For this reason mechanical vibrating
systems are coupled to electrical circuits to give an electrical output of constant frequency.
TUNING-FORK OSCILLATORS. The circuit of a tuning-fork oscillator is shown in
Fig. 12. This type of oscillator can be described as a refined buzzer. The resonant tuning
fork corresponds to the -oscillatory circuit, and the carbon button corresponds to the
vacuum tube with the carbon as the plate circuit and the diaphragm as the grid. The
feedback occurs through the transformer T. Although the electric circuit is tuned by
7-92
VACUUM-TUBE CIRCUIT ELEMENTS
O.C. fnput
FIG. 12. The Tuning Fork Oscillator
means of the transformer inductances and the capacitance C, the harmonic content of the
output is high. These oscillators are very convenient sources of audio-frequency voltage.
MAGNETOSTRICTION OSCILLATORS. When a body is placed in a magnetic field,
stresses are produced within the body tending to distort it. Inversely, when a body is
distorted, there is a change in the mag-
Tuning Fork Carbon Button netic permeability. Magnetostriction is
^ ^ * - the name given to this effect. Many
metals and alloys exhibit magnetostric-
tion, but according to Ide it is most
pronounced in alloys having 8-10 per
cent chromium, 36-38 per cent nickel,
and the remainder iron with about 1
per cent manganese to facilitate forging.
When a rod of this material is mag-
netically polarized and placed in a coil
carrying alternating current, it vibrates
longitudinally at the frequency of the
alternating current. If this frequency is
the resonant frequency of the rod me-
chanically, the amplitude of the effect
will be large even for very small currents
in the coil. Thus it can be considered
equivalent to a parallel tuned circuit coupled by means of the coil into the electric circuit.
The resonant frequency is given by v/l, where v is the velocity of sound through the rod,
about 4 km per sec, and I is the length. With the composition as above, and proper heat
treatment and magnetization, the temperature coefficient is of the order of one part in a
million per degree centigrade.
These devices are used as the oscillatory system of a vacuum-tube oscillator by means
of a circuit such as that shown in Fig. 13. An additional coil carrying direct current may
be necessary if the plate current is not sufficient to polarize the rod. Oscillations are more
easily controlled when the relation between the direction of the coils is as shown, in con-
trast to that of the Hartley circuit (Fig. la). The positive feedback is obtained by means
of the condenser C so that the electrical analogy is more nearly like the tuned-plate-tuned-
grid oscillator shown in Fig. Id. The rod is clamped in the middle (a node of its mechanical
vibration), and the ends are free to vibrate.
The frequency stability of the magnetostriction oscillator compares favorably with
that of the quartz crystal oscillators. The lower limit of frequency is determined by the
practical limit of the length of the rod. The high-frequency limit is due to the magnetic
skin effect of the rod. However, the harmonics of these high frequencies can be filtered
out of the plate circuit so that frequencies of several million
cycles can be obtained from these oscillators.
PIEZOELECTRIC CRYSTAL OSCILLATORS. With respect
to frequency, the most stable oscillators are oscillators con-
trolled by piezoelectric crystals. Crystal oscillators are used
in practically all transmitters as master oscillators. A crystal
oscillator, used by the Bureau of Standards for the broadcast of
standard frequency signals, gave a frequency stability of better
than 1.5 parts in a million over a period of a year, and its sta-
bility was better than 2 parts in 100,000,000 over a period of
several hours. By synchronizing oscillators to subharmonics of
these standards, clocks can be driven which are considerably
more accurate than pendulum clocks.
Crystal oscillators are applications of the piezoelectric effect, ~ ,0 ,™ ,, . A .
which is a means of coupling a mechanical motion to an electric Fr°' iion (^dK
circuit. When a strain is produced in a piezoelectric material,
electric charges appear on its surface. Conversely, when an electric field is produced
between surfaces of a piezoelectric material, a stress appears in the material. Thus if an
alternating electromotive force is applied between two surfaces of the material, the ma-
terial will vibrate, and if the material vibrates it will set up a displacement current between
these surfaces.
This effect has been observed in many crystals, the most important of which are: quartz,
tourmaline, and Rochelle salt (sodium potassium tartrate). Quartz and tourmaline have
been used in oscillators, quartz crystals dominating the field. Tourmaline is more expen-
mvfc than qraurt* but has the advantage that it can be ground to smaller sizes to produce
oscillators having higher frequencies.
ELECTEOMECHANICAL OSCILLATORS
7-93
[Cgp
For use in conjunction with electric circuits, these crystals are cut in slabs, the geometry
of which bears certain relations to the geometry of the crystal structure. These slabs are
mounted in crystal holders, which consist essentially of two parallel conducting plates for
the purpose of making an electrical connection with the surfaces of the crystal. An
alternating emf set up between these plates causes a current to flow because of the piezo-
electric properties of the crystal. When the frequency of this emf is equal to the mechani-
ical resonant frequency of the crystal, the conductivity between the plates is maximum.
This resonant frequency depends upon the
dimensions of the slab and upon the relation
between the geometry of the slab and the
geometry of the crystal structure. The fre-
quency of these resonators is therefore limited
by the practical limitations of size of the slab.
The frequency limits are from a few kilocycles
to a few megacycles. (See Section 13, arti-
cles 32-34.)
For the analysis of electric circuits con-
taining crystals it is convenient to replace
the crystal by its equivalent electric circuit.
This equivalent circuit is simply a series res-
onant circuit containing resistance, capac-
itance, and inductance paralleled by the
capacitance of the holder. Because of the
sharpness of tuning of this circuit, it is im-
possible actually to construct the electrical
equivalent circuit.
There are several oscillator circuits employ-
ing crystals, two of which are shown in Fig.
14. Circuit (a) makes use of the grid to plate
interelectrode capacitance for feedback, as
in the tuned-plate tuned-grid oscillator circuit
(Fig. Id) ; circuit (6) uses inductive feedback
as in the Hartley oscillator (Fig. la). As in
/*&
Quartz
Crystal
|,|rB
*ti
^7
-ilihlflu
0
o
0
^c |
0
o
0
o
(a) ,
-l|l|l|l|l|
Si
± !L
FIG. 14. Piezoelectric Crystal Oscillator Circuits
Fig. 1, the capacitances, CB, are by-pass condensers, and the inductance, LB, is a choke
coil arranged to prevent the alternating current from passing through the d-c supply source,
EB* The tuned circuits containing L and C [in (6) L = LI + Lz -f 2M] are tuned to
essentially the resonant frequency of the crystal.
The grid leaks r#, as in ordinary vacuum-tube oscillators, furnish the operating bias
for the tubes. The grid leak is in this case limited by an additional factor, namely, that
the a-c current through the crystal, which is controlled by this resistance, must not exceed
the safe operating value for the crystal. For low-frequency crystals this limit is 100 ma;
for crystals in the megacycle range it reduces to 50 ma. Above this limit the crystal may
vibrate violently enough to shatter itself. Since the d-c current through the grid leak is of
the same order of magnitude as the a-c current through the crystal, an estimate of the
value of this current can readily be obtained from the d-c grid current. In addition to this
limitation the correct value for the grid leak is governed by the operating bias for the tube
and varies from 10,000 ohms for high-^
tubes to 50,000 or more for low-/x tubes,
The circuit shown in Fig. 14a is the
most popular crystal-controlled oscillator
circuit. Wheeler has analyzed the equiv-
alent of this circuit (Fig. 15) by the
method of van der Pol for the theory of
non-linear oscillators. He obtained certain
criteria for the frequency to be dependent
- -An j« »i primarily upon the resonant frequency of
nmt Correspond^! to ^ ^^ ^^ ^ Q of the plate oircuit
tuning coil, i.e., the L to r ratio, should be
as small as is consistent with stable oscillation. Second, the plate resistance of the tube
should be as high as is consistent with stable oscillation. Third, CA, which includes the
capacitance Cf and the grid to filament tube capacitance as well as the crystal holder
capacitance, should approach but not exceed p — 1 times Cgp. Fourth, the plate tuning
capacitance, C, should be adjusted to give maximum plate current.
The plate resistance can be made large by the choice of the tube and by decreasing the
operating plate voltage. The capacitance Ck is usually made enough smaller than Cgp
te
. 15.
7-94
VACUUM-TUBE CIECUIT ELEMENTS
D.C. Field Supply
Output
(a - 1) 80 that €f may be used as a fine adjustment of the frequency. The resonant
frequency of the resonant circuit in the plate circuit must be above the resonant frequency
of the crystal, while, if this resonant circuit has too high a frequency the plate load imped-
ance is so low that oscillations cannot exist. As the capacitance, C, is varied from too low
a value toward that value at which the resonant frequency of the plate circuit is the same
as that of the crystal, the circuit at first fails to oscillate, then feeble oscillations start
which increase steadily until just before the critical frequency the amplitude of osculation
rapidly drops to zero. The total variation in frequency of oscillation throughout this
adjustment is 2 to 5 parts in 10,000. The optimum adjustment is for C to have a value
just less than that for critical frequency.
Without some special means of temperature control, the resonant frequency of the
crystal itself changes. The temperature coefficients of crystals vary, depending upon the
relation between the geometry of the slab and the geometry of the crystal structure, from
1 part in 10,000 to 1 part in a million or less per degree centigrade. To minimize the
variation in frequency due to the temperature, elaborate temperature-controlled ovens
are used to maintain the temperature constant to better than 0.01 deg cent. For frequency
control of an ordinary transmitter, ovens capable of maintaining temperatures to within
0.1 deg are sufficiently accurate.
A crystal oscillator may be designed to supply as much as 10 watts of output power at a
plate efficiency of 30 to 60 per cent. The plate current and power output are limited by the
current through the crystal. The usual d-c plate voltage is from 200 to 400 volts.
Because of the low power output and in order to prevent feedback into the crystal, a
buffer amplifier must be used between these oscillators and the place where the power is to
be applied, especially when the load is variable
as in modulation.
ALTERNATORS. Alternators are used pri-
marily to produce a-c power at the low fre-
quencies employed in power engineering. How-
ever, before the advent of high-power vacuum
tubes, comparatively high frequencies for use in
communication were obtained from specialized
alternators. Two types of alternators were
extensively employed for this purpose.
Alexanderson Alternators. The schematic
diagram of an Alexanderson alternator is shown
in Fig. 16. The toothed wheel is rotated be-
tween the poles of the magnet energized by a d-c field coil. This changes the magnetic
flux density through the output coil periodically, setting up alternating currents in the load.
The frequency of these alternators is limited to about 200 kc by the obvious mechanical
limitations of construction and operation as well as by losses in the iron core and teeth.
_ Goldsdunidt Alternators. The Goldschmidt alternators operated on a different prin-
ciple. In a low-frequency single-phase alternator, the electromotive force developed
in the armature contains not only the fundamental frequency but also the odd harmonics.
Similarly, the field contains the even harmonics. Ordinarily, the reactances of the circuits
are so arranged that the impedances to the fundamental and to the harmonics present are
relatively high. The Goldschmidt alternators are designed so that the impedance at the
frequencies of these harmonics is low. Then, by means of filters, one of the higher har-
monics, usually the fourth harmonic, is selected for use. The frequency is limited here to
about the same value by the same factors as in the Alexanderson alternator
SPARK-GAP OSCILLATORS. Most of the early radio telegraph transmitters were
damped-wave transmitters. These damped-wave oscillations were produced by means of
spark-gap oscillators. The circuit of
one of these oscillators is shown in . Spark Gap
Fig. 17. When the instantaneous
voltage across the spark gap due to
the audio-frequency generator ex-
ceeds the breakdown potential of the
gap, a sudden rush of current shock-
exwfces the oscillatory circuit consist-
ing of tbe inductance L and the
capacitance C, setting up an oscilla-
tory eojireot wfeieh is damped out
bf tbe resistance of the inductor,
Toothed Rotor
FIG. 16. Alexander-son Alternator
Audio
Frequency
Generator
f
Audio Frequency
Transformer
FIG. 17. Spark-gap Oscillator
and by the load. The low resistance of the discharg-
ing are m negligible imtil the voltage across it drops below some comparatively small value
Thw oemri twice duiing each cycle of the audio frecpiency. The most prominent frequency
CAVITY RESONATOBS 7-95
in the output is the natural frequency of the resonant circuit, i.e., - — 7=:* The out-
put may be considered a carrier of this frequency modulated by an audio having a fun-
damental of twice the frequency of the generator voltage. There are so many harmonics
of the audio that the bandwidth necessary for this type of transmission is very wide. For
this reason, the ordinary use of spark transmitters is prohibited by law. However, many
emergency stand-by transmitters on ships are of this type. The audio-frequency gen-
erator is frequently a buzzer using the transformer primary as the coil so that these trans-
mitters may be operated by means of a battery.
Spark-gap transmitters are actively used at the present time for many industrial appli-
cations, chiefly to supply induction furnaces. The spark gaps are usually not ah* gaps, but
a discharge in mercury vapor alone or with hydrogen. Such gaps can deliver high power
at high efficiency, and they compare favorably with vacuum-tube oscillators for this
purpose.
BIBLIOGRAPHY
Andrew, Victor J., The Adjustment of the Multivibrator for Frequency Division, Proc. I.R.E., Vol.
19, 1911 (1934).
Fay, C. E., and A. L. Samuel, Vacuum Tubes for Generating Frequencies above 100 Megacycles,
Proc. I.R.E., Vol. 23, 199 (1935).
Hayasi, Tatuo, The Inner-grid Dynatron and the Duodynatron, Proc. I.R.E., Vol. 22, 751 (1934).
Ide, John McDonald, Magnetostriction Alloys with Low Temperature Coefficients, Proc. I.R.E., Vol.
22, 177 (1934).
Kelster, Frederick A., Generation and Utilization of Ultra-short Waves in Radio Communication,
Proc. I.R.E., Vol. 22, 1335 (1934).
Lapham, E. G., A 200-kilocycle Piezo Oscillator, Bur. Standards J. Research, Vol. 11, 59 (1933).
Llewellyn, F. B., Constant-frequency Oscillators, Proc. I.R.E., Vol. 19, 2063 (1931).
Llewellyn, F. B., Note on Vacuum-tube Electronics at Ultra High Frequencies, Proc. I.R.E., Vol. 23,
112 (1935).
MacKinnon, K. A., Crystal Control Applied to the Dynatron Oscillator, Proc. I.R.E., Vol. 20, 1689
(1932).
Mcllwain, Knox, and J. G. Brainerd, High-frequency Alternating Currents. John Wiley (1939).
Miles, L. D.f A New Source of Kilocycle Kilowatts, Elec. Engg., Vol. 305, 54 (1935).
Moore, W. H., Electron Oscillations without Tuned Circuits, Proc. I.R.E., Vol. 22, 1021 (1934).
Morrison, W. A., A High Precision Standard of Frequency, Proc. I.R.E., Vol. 17, 1103 (1929).
Peterson, E., J. G. Kreer, and L. A. Ware, Regeneration Theory and Experiment, Proc. J.B.E., Vol.
22, 1191 (1934).
Prince, D. C., and F. B. Vogdes, Vacuum Tubes as Oscillation Generators. General Electric Review,
Schenectady, N. Y. (1929).
Schneider, E. G., Radar, Proc. I.R.E., Vol. 34, 528 (1946).
Terxnan, F. E., Radio Engineering. McGraw-Hill (1932).
Terman, F. E., R. R. Buss, W. R. Hewlett, and F. C. Cahill, Some Applications of Negative Feed-
back with Particular Reference to Laboratory Equipment, Proc. I.R.E., Vol. 10,649 (1939).
Thompson, B. J., and G. M. Rose, Jr., Vacuum Tubes of Extremely Small Dimensions for Use at
Extremely High Frequencies, Proc. I.R.E., Vol. 21, 1707 (1933).
Thompson, B. J., and P. D. Zottu, An Electron Oscillator with Plane Electrodes, Proc. I.R.E., Vol. 22,
1374 (1934).
van der Pol, Balth, The Non-linear Theory of Electric Oscillations, Proc. I.R.E., Vol. 22, 1051 (1934).
Wheeler, L. P., Analysis of a Piezoelectric Oscillator Circuit, Proc. I.R.E., Vol. 19, 627 (1931).
22. CAVITY RESONATORS
By L G. Wilson and J, P. Kinzer
A cavity resonator is a section of dielectric completely surrounded by a metallic shell.
In many ways, its performance is analogous to a resonant R, L, C low-frequency circuit.
However L, C, and R can no longer serve as basic in the consideration of cavity resonators,
because of the inability to define inductance and capacitance uniquely. (See reference 1.)
In fact it is possible to find only two such quantities which describe the properties of a
cavity resonator.
The first of these is the resonant frequencies (or wavelengths) , defined as those values of
/ (or X) which result in the boundary conditions being satisfied. With each resonance
there is associated a particular standing-wave pattern of the electromagnetic fields,
These have been called "eigenvalues" or "eigentones," but the term "normal modes" is
now in general use.
The second is the quality factor, Q, defined by
Energy stored
Energy lost per cycle
7-96
VACUUM-TUBE CERCTJIT ELEMENTS
o o
A A
o o
A A
o5 O JH
fill
'
II ft
.98 §.2
n
1
n n n
I
n
te!
CAVITY RESONATORS
7-97
A
g
o o
A A
a s
^ 8
g b
a &
o o
8 £
*
2 2
& -i
n n n
0. qS N
ttj KJ HS
•a •§
2 2
1
S
I
*tl
IZi
7-98
VACUUM-TUBE CIRCUIT ELEMENTS
ss
*•§
.s
I
2
•g
OQ
|
12
Q
a
I
"o
a
A
i s s
Hi ° ^
"a S
-3 J
A A
S >s
c ?
pp
I 1
j I
I £
X 5
? i
1 1
-2
1
CAVITY RESONATORS
7-99
>-A ! t
II
or Q -
•§
I
o
^H
J2
3
+
4-
+ ,3
Vt
/\
s
A
e
+
H|
£
i
+
-
65
"«»• Jl t
*
a +
e e
ii a n
fe; ^ Os
S o
I
61*
g «
*3 *
-§._§
^•j
s
a
5
7-100
VACUUM-TUBE CIRCUIT ELEMENTS
Q
i|j &
it n n
-i
I
±
«
,0
01
£-t
A H
Approximation for
Tot Number of
M TE and
aving
m
u
odes (
TM) Ha
t
CAVITY RESONATORS 7-101
In calculating X, the assumption is made that the walls of the cavity have perfect con-
ductivity. When Q is calculated, the assumption is made that X is unchanged; that is, the
fields that actually exist are those calculated on the basis of perfectly conducting walls.
Since the Q's are generally high, the approximation is extremely good. (See reference 2.)
Since the energy is stored in the cavity volume, while the energy is lost in the walls, to
obtain a high Q, the resonator should have a large ratio of volume to surface area. For
this reason, cylinders, prisms, or spheres will in general have better Q*s than cavities with
re-entrant portions, or coaxial structures.
In computing the resonant frequencies and Q values of cavity resonators, solutions of
the field equations involve, for the rectangular prism, circular functions; for the perfect
cylinder, Bessel functions of the first kind; and, for two coaxial cylinders, Bessel functions
of the first and second kinds. Only approximate solutions have been derived for cavities
involving re-entrant sections.
MODES. By fundamental and general consideration, the modes in every cavity reso-
nator, regardless of its shape, are infinite in number and more closely spaced as the fre-
quency increases. The total number, N, of these having a resonant frequency less than
/ is given approximately by:
N- = g VJ» (6)
where V = volume of cavity in cubic meters.
c = velocity of electromagnetic waves in the dielectric in meters per second.
/ — frequency in cycles per second.
PRINCIPLE OF SIMILITUDE. Another theorem generally applicable to all cavities
is the principle of similitude, stated as follows (see reference 3): A reduction hi all the
linear dimensions of a cavity resonator by a factor 1/ra (if accompanied by an increase in
the conductivity of the walls by a factor m) will reduce the wavelengths of the modes by
the factor \{m. For high-Q cavities, the condition given in parentheses need not be
considered.
MODES IN RIGHT CYLINDERS. In right cylinders (ends perpendicular to axis)
the modes fall naturally into two groups, the transverse electric (TE) and the transverse
magnetic (TM). In the TE modes, the electric lines everywhere lie in planes perpendicu-
lar to the cylinder axis, and in the TM modes the magnetic lines so lie. Further identifi-
cation of a specific mode is accomplished by the use of indices.
THE MS FACTOR. With a cylinder restricted to a loss-free dielectric and a non-
magnetic surface, the value of Q (quality factor) for each mode depends on the conduc-
tivity of the metallic surface, the frequency, and the ratio of a cross-sectional dimension
to the length. The quantity Q5/X, however, depends only upon the mode and shape and is
referred to as the mode-shape (MS) factor.
In this expression, 5 refers to skin depth (see reference 4) in meters = (l/2ir) (Vl07p//),
X is wavelength in meters in the dielectric == c//, and p the resistivity in ohm-meters.
The skin depth is a factor which recognizes the dissipation of energy in the walls and ends
of the cylinder. With increase of resistivity of these surfaces the currents penetrate
deeper and the resulting Q is lower.
FUNDAMENTAL FORMULAS. Expressions for standing-wave patterns and Qd/\
are given in Table 1, for right rectangular, circular, and full coaxial cylinders. The mode
indices are Z, m, n following the notation of Barrow and Mieher (reference 5). In the
rectangular prism they denote the number of half-wavelengths along the coordinate axes.
For the other two cylinders they have an analogous physical significance with Z related to
the angular coordinate, m to the radial, and n to the axial.
In an elliptical cylinder, a further index is needed to distinguish between modes which
differ only in their orientation with respect to the major and minor axes; these paired
modes are termed even and odd and have slightly different resonant frequencies (see
reference 6) . In the circular cylinder they have the same frequency, a condition which is
referred to as a degeneracy (in this case, double) ; that is, in the circular cylinder, odd and
even modes are distinguishable only by a difference in their orientation within the cylinder
with reference to the origin of the angular coordinate. In Table 1, the field expressions
are given for the even modes; those for the odd modes are obtained by changing cos Id to
sin W and sin IB to cos IB everywhere.
The value of N in the table for the circular cylinder is based on counting this degeneracy
as a single mode; counting even and odd modes as distinct will nearly double the value of
N, thus bringing it into agreement with the general eq. (6) .
In Table 1, the mks system of units is implied. The notation is in general accordance
with that used in prior developments of the subject. For engineering applications, it is
advantageous to reduce the results to units in ordinary use and to change the notation
7-102
VACUUM-TUBE CIRCUIT ELEMENTS
wherever this leads to a more obvious association of ideas. For these reasons, in what
follows attention is confined to the right circular cylinder, with changes in units and
notation as specified later.
4,0
FIG. 18. Mode Chart for Circular Cylinder Cavity Resonator. Z> and L in inches- / in megacycles
per second. The rectangle indicates the best operating region for the TE Oil mode,
THE MODE CHART. The formula relating the resonant frequency to the mode,
shape, and dimensions may be written simply:
C/D}* = A + Bn* (2V (7)
frequency in megacycles per second.
D =» diameter of cavity in inches.
L = length of cavity in inches.
4 * a csoastaat depending upon the mode. Values of A are given in Table 2 for
Ifee kwesfe 30 modes. Values of Bessel function roots are given in Table 3
lor fafc 180 modes.
CAVITY RESONATORS
7-103
B = a constant depending upon the velocity of electromagnetic waves in the dielec-
tric. For air at 25 deg cent and 60 per cent relative humidity, B = 0.34799 X
108.
n - third index defining the mode, i.e., the number of half wavelengths along the
cylinder axis.
Formula (7) represents a family of straight lines, when (D/£)2 and (/D)2 are used as co-
ordinates, and leads directly to the easily constructed and highly useful mode chart of
Fig. 18.
It will be noted from Table 2 that the TE Qmn and the TM Imn modes have the same
frequency of resonance. This is a highly impor-
tant case of degeneracy. In the design of prac-
tical cavities it is necessary to take measures to
eliminate this degeneracy, as the TM mode (usu-
ally referred to as the companion of its associated
TE mode) introduces undesirable effects.
DESIGN OF HIGH-Q CAVITY IN TE Oln
MODE. In many applications, a resonator is
used in its fundamental (gravest) mode. How-
ever, when high values of Q are desired, it may
be necessary to use a high-order mode. In this
case, it is desirable to keep the volume the mini-
mum because other modes can cause undesired
responses and other deleterious effects. As shown
by eq. (6), the total number of resonances is a
function of the volume. Analysis of the problem
leads to the conclusion that operation in the TE
Oln mode (unimportant exceptions occur for
values of Q5/\ less than 1.2) gives the smallest
volume for an assigned Q and also leads to specific
values of n and D/L which give this result. In
fact, for maximum Q per volume in the TE Oln
mode,
Table 2. Constants for Use in Com-
puting the Resonant Frequencies of
Circular Cylinders
B
• 0.34799 X 10s
1.17981 X 1010 in. per sec
= 3.11 X 108
(8)
which permits easy plotting on a mode chart of
the locus of the operating points for best Q per
volume ratio.
The mode-shape (MS} factor for the TE Oln
modes may be expressed as follows:
2.77
1 + 0.168 —
This has been derived from Table 1 by com-
bining terms which are a function of frequency
and by assuming the conductivity of copper
(p = 1.7241 X 10~8 - the International Stand-
ard value for copper) for the cylinder walls.
The relative Q's for several metals are: silver
1.03, copper 1.00, gold 0.84, aluminum 0.78, and
brass 0.48. Therefore, a brass cavity will have
Mode
r
A
TM 01
2.40483
0. 81563 X 10s
02
5.52008
4.2975
03
8.65373
10.5617
n
3.83171
2.0707
12
7.01559
6.9415
13
10.17347
14.5970
21
5.13562
3.7197
22
8.41724
9.9923
31
6.38016
5.7410
32
9.76102
13.4374
41
7.58834
8.1212
51
8.77148
10.8511
61
9.93611
13.9238
TE 01
3.83171
2.0707
02
7.01559
6.9415
03
10.17347
14.5970
11
1.84118
0.47810
12
5.33144
4.0088
13
8.53632
10.2770
21
3.05424
1.3156
22
6.70613
6.3426
23
9.96947
14.0175
31
4.20119
2.4893
32
8.01524
9.0606
41
5.31755
3.9879
42
9.28240
12.1520
51
6.41562
5.8050
61
7.50127
7.9359
71
8.57784
10.3772
81
9.64742
13.1265
Value of c is for air at 25 deg cent and 60
per cent relative humidity. D and L in
inches ; / in megacycles.
about one-half of the Q of a similar copper cavity. Silver-plating a copper cavity will
increase Q about 3 per cent. Experience shows that only 80 to 90 per cent of the theo-
retical Q can be realized. This should be taken account of in the design.
With the frequency and desired Q known, the dimensions of the cavity can be deter-
mined.
CAVITY COUPLINGS. To be useful the cavity must be coupled to external circuits.
The coupling to all modes can be analyzed, at least qualitatively, from the field expres-
sions of Table 1. The problem is to get the correct coupling to the desired mode and as
little coupling as possible to all others. This may be obtained either by a loop or a probe
at the end of a coaxial line or by an orifice connecting the cavity with a wave guide. For
optimum coupling the plane of a loop must be perpendicular to the H lines; the axis of a
7-104
VACUUM-TUBE CIRCUIT ELEMENTS
probe must be colHnear with the E lines; and the H lines in a wave guide feeding through
an orifice must be parallel to the H lines in the cavity. ^
Since the electric field is zero everywhere at the boundary surface of the cavity for the
TE Oln mode, coupling to it must be magnetic; a probe cannot be used. The location for
Table 3. Values of the Bessel Function Zero (rZm) for the First 180 Modes in a Circular
Cylinder Resonator
Tim
Mode*
rim
Mode
rjm
Mode
rjm
Mode
\ 1.8412
E 1-1
46 13,0152
M 3-3
91 18.4335
M 10-2
136 22.6716
E 2-7
2 2.4048
M 0-1
47 13.1704
E 2-4
92 18.6374
E 6-4
f!37 22.7601
M 1-7
5 3.0542
E 2-1
M8 13.3237
M 1-4
93 18.7451
E 12-2
I 138 22.7601
E 0-7
( 4 3.8317
M 1-1
I 49 13.3237
E 0-4
94 18.9000
M 14-1
139 22.9452
M 8-4
{ 5 3.8317
E 0-1
50 13.3543
M 9-1
95 18.9801
M 5-4
140 23.1158
M 14-2
6 4 . 20 1 2
E 3-1
51 13.5893
M 6-2
96 19.0046
E 9-3
141 23.2548
E 21-1
7 5.1356
M 2-1
52 13.8788
E 12-1
97 19.1045
E 17-1
142 23.2568
M 18-1
8 5.3176
E 4-1
53 13.9872
S 5-3
98 19.1960
E 4-5
143 23.2643
E 16-2
9 5.3314
E 1-2
54 14.1155
S 8-2
99 19.4094
M 3-5
144 23.2681
E 7-5
10 5.5201
M 0-2
55 14.3725
M 4-3
100 19.5129
E 2-6
145 23.2759
M H-3
11 6.3802
M 3-1
56 14.4755
M 10-1
101 19.5545
M 8-3
146 23.5861
M 6-5
12 6.4156
E 5-1
57 14.5858
E 3-4
f 102 19.6159
M 1-6
147 23.7607
E 10-4
13 6.7061
E 2-2
58 14.7960
M 2-4
1 103 19.6159
E 0-6
148 23.8036
E 5-6
f 14 7.0156
M 1-2
59 14.8213
M 7-2
104 19.6160
M 11-2
149 23.8194
E 13-3
( 15 7.0156
E 0-2
60 14.8636
E 1-5
105 19.8832
E 13-2
150 24.0190
M 4-6
16 7.5013
E 6-1
61 14.9284
E 13-1
106 19.9419
E 7-4
151 24.1449
E 3-7
17 7.5883
M 4-1
62 14.9309
M 0-5
107 19.9944
M 15-1
152 24.2339
M 9-4
18 8.0152
S 3-2
63 15.2682
S 6-3
108 20.1441
E 18-1
153 24.2692
M 15-2
19 8.4172
U 2-2
64 15.2867
B 9-2
109 20.2230
E 10-3
154 24.2701
M 2-7
20 8.5363
E 1-3
65 15.5898
M 11-1
110 20.3208
M 6-4
155 24.2894
E 22-1
21 8.5778
S 7-1
66 15.7002
M 5-3
111 20.5755
E 5-5
156 24.3113
E 1-8
22 8.6537
M 0-3
67 15.9641
E 4-4
112 20.7899
M 12-2
157 24.3382
M 19-1
23 8.7715
M 5-1
68 15.9754
E 14-1
113 20.8070
M 9-3
158 24.3525
M 0-8
24 9.2824
E 4-2
69 16.0378
M 8-2
114 20.8269
M 4-5
159 24.3819
E 17-2
25 9.6474
E 8-1
70 16.2235
M 3-4
115 20.9725
E 3-6
160 24.4949
M 12-3
26 9.7610
M 3-2
71 16.3475
E 2-5
116 21.0154
E 14-2
161 24.5872
E 8-5
27 9.9361
M 6-1
72 16.4479
E 10-2
117 21.0851
M 16-1
162 24.9349
M 7-5
28 9.9695
IS 2-3
f 73 16.4706
M 1-5
118 21.1170
M 2-6
163 25.0020
E 14-3
{ 29 10.1735
M 1-3
174 16.4706
E 0-5
119 21.1644
E 1-7
164 25.0085
E 11-4
} 30 10.1735
E 0-3
75 16.5294
E 7-3
120 21.1823
E 19-1
165 25.1839
E 6-6
31 10.5199
E 5-2
76 16.6982
3f 12-1
121 21.2116
Jf 0-7
166 25.3229
J£ 23-1
32 10.7114
E 9-1
77 17.0038
M 6-3
122 21.2291
j£ 8-4
167 25.4170
M 16-2
33 11.0647
M 4-2
78 17.0203
S 15-1
123 21.4309
E 11-3
168 25.4171
M 20-1
34 11.0864
M 7-1
79 17.2412
Jtf 9-2
124 21.6415
M 7-4
169 25.4303
M 5-6
35 11.3459
£ 3-3
80 17.3128
E 5-4
125 21.9317
E 6-5
170 25.4956
E 18-2
36 11.6198
M 2-3
81 17.6003
# 11-2
126 21.9562
M 13-2
171 25.5094
Jf 10-4
37 11.7060
^ 1-4
82 17.6160
M 4-4
127 22.0470
If 10-3
172 25.5898
# 4-7
38 11.7349
S 6-2
83 17.7740
J£ 8-3
128 22.1422
E 15-2
173 25.7051
M 13-3
39 11.7709
E 10-1
84 17.7887
.E 3-5
129 22.1725
M 17-1
174 25.7482
Jf 3-7
40 11.7915
Jfcf 0-4
85 17.8014
M 13-1
130 22.2178
M 5-5
175 25.8260
E 2-8
41 I2.225T
M 8-1
86 17.9598
jfcf 2-5
131 22.2191
# 20-1
176 25.8912
J£ 9-5
42 12.3386
If 5-2
87 18.0155
E 1-6
132 22.4010
tf 4-6
f 177 25.9037
Af 1-8
43 12.6819
E 4-3
88 18.0633
£ 16-1
133 22.5014
E 9-4
I 178 25.9037
E 0-8
44 12.8265
s u-r
89 18.0711
Jfef 0-6
134 22.5827
Jf 3-6
179 26.1778
J£ 15-3
45 12.9324
£ 7-2
90 18.2876
M 7-3
135 22.6293
E 12-3
180 26.2460
E 12-4
* Nomenclature after Barrow and Mieher, Natural Oscillations of Electrical Cavity Resonators
Free. I.R.E., April 1940, p. 184.
M modes take zeros of Jj<x) ; ^ modes take zeros of Jz'fcc). Number directly following E or AT is Z;
number after hyphen is number of root.
Values less than 16.0 are abridged from six-place values and are believed to be correct; values more
than 16.0 are abridged from five-place values and may be in error by one unit in fourth decimal place.
Underlined 5 in fourth place indicates that higher value is to be used in rounding off to fewer decimals."
maximum coupling is on the side of the cavity, an odd number of quarter-guide wave-
lengths from the end, or on the end about halfway (48 per cent) out from the center to the
ed«©. Correct orientation requires the axis of a loop to be parallel to the axis of the
cylmder for side-wail feed and to be perpendicular to the cylinder axis for end feed. Wave-
guide orientation is shown in Table 4.
Tfee theory of coupling loops and orifices is not at present precise enough to yield more
tfean approximate c&rmnsions. On the basis of rather severely limiting assumptions,
coupling fonaiiias for a round hoie connecting a rectangular wave guide and a TE Oln
CAVITY RESONATORS
7-105
CD
ro
CD
cu
QOH13W QNHdnOO
UJ UJ
2 2
I
Q
u
^3
— CO O
s 2 a
c o - o
fc •* rt o>
£ w — q
d d d
So N
53 P
£ S S 2
odd
^ » s a
O — <vi
i § §
UJ UJ UJ
H I- I-
&1NV1SNOO
ll:
CVJ Z CO
LU O :
^ 5 i
sis
U. ? O
IFICE
VITY
X
£
5
z
^ >
co>
>
7-106 VACUUM-TUBE CIRCUIT ELEMENTS
cavity are given on Table 4. The assumptions are that the orifice is in a wall of negligible
thickness, its diameter is small compared to the wavelength, it is not near any surface
discontinuity, and the wave guide propagates only its principal (gravest) mode and is
perfectly terminated. In some applications, the computed diameter is somewhat smaller
than experiment shows to be correct.
Coupling by means of an electron beam can also be used, but, owing to transit time, a
re-entrant-type cavity is usually used to keep down the distance the electrons must travel
within the resonator.
BIBLIOGRAPHY
1. Hanaen, W. W., and R. D. Richtmyer, On Resonators Suitable for Klystron Oscillators, J. Applied
2. HanaSn,' W? W.% Type of Electrical Resonator, J. Applied Phys., Vol. 9, 654-663 (1938). .
3. K6nig, H.f The Laws of Similitude of the Electromagnetic Field, and Their Application to Cavity
Resonators, Hochf. tech u. Elek:akust Vol. 58, 174-180 (1941). Also Wireless Engineer, Vol. 19,
216-217, No. 1304 (1942).
4. Wheeler, H. A., Formulas for the Skin Effect, Proc. I.R.E., Vol. 30, 412-424 (1942).
5. Barrow, W. L., and W. W. Mieher, Natural Oscillations of Electrical Cavity Resonators, Proc.
6. Chu, L'j,, Electromagnetic Waves in Elliptical Hollow Pipes of Metal, /. Applied Phys., 9, 583-
591 ( 193S)
7. Borgnis, F., Elektromagnetisehe Eigenschwingungen dielektriseher Raume, Ann. Physik, Vol. 35,
35&-3S4 (1939).
a Borgnis, F.t Die konzentrische Leitung als Resonator, Hoctif. tech u. Elek:akus, Vol. 56, 47-54
(1940). Resonant modes and Q of the full coaxial resonator. For long abstract, see Wireless
Engineer, Vol. 18, 23-25 (1941).
9. Wilson, I. G., G. W. Schramm, and J. P. Kinzer, High Q Resonant Cavities far Microwave Test-
ing. B.S.T.J., Vol. 25, 408-434 (1946).
10. Kinzer, J. P., and I. G. Wilson, End Plate and Side Wall Currents in Circular Cylinder Cavity
Resonator. B.S.T.J. Vol. 26, 31-79 (1947).
11. Kinzer, J. P., and I. G. Wilson, Some Results on Cylindrical Cavity Resonators. B.S.T.J. Vol.
26, 410-445 (1947).
POWER SUPPLY
By J. E. Young
23. RECEIVER POWER SUPPLY
The first receivers to employ vacuum tubes used batteries for filament and plate power
supplies, but tubes were soon developed which had cathodes suitable for heating by
alternating current. At the same time rectifier-filter combinations were developed to sup-
ply plate voltage, and it was no longer necessary to depend on batteries, where a-c power
was available. During the ensuing years the size of batteries has been reduced, and their
shape has been adapted to receiver applications. At the same time their life has been
considerably increased. Batteries are now used extensively in receivers in areas where no
power is available and for portable receivers which are often designed so that either bat-
tery or a-c power may be used. Sealed storage batteries have also been developed, and
receivers using them arranged so that, if the receiver is plugged in an a-c line, the batteries
are automatically recharged.
FILAMENT POWER. - The filament power for a-c operated receivers is usually ob-
tained from one or more windings of the receiver power transformer. The design of power
transformers is covered on pp. $-26 to 6-30. A common winding is customarily employed
to excite all cathodes; however, it sometimes happens that both filamentary and indirectly
heated cathode tubes are used in a receiver, and bias is applied to the filamentary tubes
in such a way that the filament winding of the transformer is maintained at a potential
considerably above ground. It is possible, in this case, that the difference in potential
between the cathode and heater of the indirectly heated tubes will exceed the value
specified by the tube designer. Where this condition exists, or where, because of the
circuits in which the cathodes of the tubes are connected, it may likewise be possible to
exceed the rated potential difference between the cathode and the heater for which the
tube was designed, it is necessary to provide separate filament windings, grouping the
tubes on these windings in such a manner that excessive voltage strain will not exist
between cathode and heater of any tube.
MATE POWER. The voltage supply for the plate circuits of the receiving tubes in
a modem receiver is usually obtained from a vacuum-tube rectifier. A high a-c voltage
is applied to the tube, and the rectified output is passed through a low-pass filter to atten-
uate the a~c components. In Fig. 1 a typical B supply circuit is shown. With a condenser
RECEIVER POWER SUPPLY
7-107
f
Fl
3O f
Ctic
lenry
"kes
•nfflRHT*
Z2 5
i
J~
C3
A*.
\
\
\
I
Filament
<r — r!>-T-
Suppfy
t
Voltage
B 1 i o
T4= 1 =
UJ
•)oiooJ
j. l— »
! \
115 Volts
(Rms.)
Rectifier
122 Vi'V I
Tap |
iFor Choke Inpat
Omit Ct
• Fitter -
-Qatptrt Systei
FIG. 1. Typical Receiver Power Supply
60^Applied Voltage
Current In
1st Plate
Current in
2nd Plate
5afhode
Current
60/v.ApplLed Voliage
Cuaenf in 1st Plate
Current In 2nd Plate
Cathode Cm-cent
Condenser Input Choke
FIG. 2. Wave Form in Rectifier Circuits
7-108
VACUUM-TUBE CIRCUIT ELEMENTS
input to the B filter (Ci connected) the ratio of d-c output voltage to a-c input voltage is
higher than with a choke input (Ci disconnected). The choke input has the advantage of
lower peak currents with less danger of damage to the tube under overload conditions.
The voltage regulation with variable load is also better with choke input.
In Fig. 2 the form of the currents and voltages is given for various portions of these
two circuits.
Figures ZA and SB illustrate the relations between output voltage and load current for
a typical full-wave rectifier for a choke input filter circuit and for a condenser input filter
circuit.
520
40 80 120
D,C. Load MHfiamperes
A. Choke Input to Filter.
12.0
40. 80 120 160
D.C- Load Mliriamperes
B. Condenser Input to Filter.
FIG. 3. Output Characteristics of Rectifier Tubes
MERCURY- VAPOR RECTIFIERS. The efficiency of rectification is improved by the
presence of mercury vapor in the tube. The mercury vapor reduces the voltage drop in
the tube and improves the voltage regulation. This type of tube may produce r-f inter-
ference unless special precautions are taken, such as shielding of the rectifier tube and the
use of r-f chokes or resistors hi the rectifier plate leads.
B SUPPLY FILTER. The capacitor input filter is the most economical type if the
transformer impedance and rectifier tube type are such that excessive charging current
will not be experienced. In general, electrolytic capacitors are compact and inexpensive
enough so that filters are usually designed with a rather large ratio of capacitance to in-
ductance. It frequently happens that tubes, or the elements of tubes used for different
purposes in the receiver, require different voltages. In this event it is economical to ob-
tain additional filtering by using the voltage drop resistors and shunt capacitors as a
resistance-capacitor filter. Since the capacitive reactance will generally be small com-
pared to the resistance, the attenuation of this type of filter is inversely proportional to
the product of the resistance and capacitance. If this is so, sufficient filtering is provided
in the main filter to produce the required ripple attenuation for the tubes which are sup-
plied directly from this filter.
It is possible to obtain increased attenuation by substituting a shunt resonant circuit
for the inductive element of the filter; however, this practice is rarely followed, since the
attenuation of ripple frequencies higher than the resonant frequency of the circuit is
reduced and it is costly, in production, to maintain the values of inductance and capaci-
tance closely enough to insure resonance at the correct frequency. The speaker field is
frequently used as one of the chokes of the filter, and occasionally a hum-bucking coil is
provided on the voice coil of the loudspeaker.
24. TRANSMITTER POWER SUPPLY
A-C POWER. A-c power is used for filament and plate supplies for transmitters
almost universally. Filaments are usually heated by alternating current directly ; rectifier-
filter systems are provided for plate and bias supplies. Where alternating current is not
available, motor generators or, for very low power transmitters, batteries are used.
TRANSMITTER POWER SUPPLY 7-109
FILAMENT POWER. Small transmitting tubes, unless used in service requiring
quick-heating types, usually have indirectly heated cathodes. Unipotential cathodes
are also required to permit operation at very high radio frequencies. Considerations
affecting the design of filament power supplies for such tubes are covered in Section 6, ar-
ticle 14. Large tubes are usually directly heated and have either a tungsten filament or,
where practicable, a thoria-coated tungsten filament. The emission efficiency of the latter
is higher and less filament power is, therefore, required to achieve a given space current.
Filament power is usually derived from a 115- or 230-volt bus connected to the trans-
mitter supply through a regulator, rheostat, or other means of holding the filament voltage
within required limits (generally ±5 per cent), and necessary control switches and protec-
tive devices. Step-down transformers convert the bus voltage to a value suitable for
application to the filaments of the tubes. It should be noted that the life of tungsten-
filament tubes is greatly affected by small changes in voltage. It is advisable, therefore,
to provide means of adjusting the filament voltage of each such tube independently. The
filament voltage should be no higher than is required to provide the necessary emission
current.
FILAMENT STARTING. The cold resistance of transmitting-tube filaments is gen-
erally less than a tenth of the hot resistance. Filament-heating currents are usually large
enough to cause severe mechanical stresses in the filaments and their supports. It is
necessary, therefore, to limit the filament starting current to a safe value. This is de-
termined by the designer of the tube and is frequently specified as one and one-half times
the normal running current. Starting-current limitation is secured either by applying the
filament voltages in steps, controlled so that the current reaches a steady value before
the next voltage increment is applied, or by using a current-Umiting reactor in the filament
transformer primary circuit. The necessary reactance may be designed into the filament
transformer itself, or a separate reactor may be used. This method of- limiting filament
current is preferable since the voltage increase across the filament terminals is smooth and
is directly controlled by the filament resistance.
HUM DUE TO FILAMENT CURRENT. The electron stream emitted by the fila-
ment is affected by the magnetic field set up around the filament by the heating current.
This effect is a periodic change in the space impedance between the filament and each of
the other elements of the tube, at twice the frequency of the filament exciting current.
The magnitude of this effect is a function of the design of the tube. The transmitter
designer may minimize it either by the use of a tube having a multistrand filament con-
nected to a two- or three-phase heating source, or by heating the filaments of tubes con-
nected in pushpull or parallel from different phases of a two- or three-phase power supply.
Tubes connected in pushpull and delivering power to the load at different parts of the
audio-frequency cycle should have their filaments heated by currents which' are in phase.
The reduction of ripple obtained by multiphase filament connection will generally be of
the order of 10 db for a two-phase filament connection and 14 db to 18 db for three-phase.
The improvement obtained by the use of more than three phases is small, and the in-
creased sensitivity of the ear to the higher resulting ripple frequency may make the hum
more objectionable.
PLATE POWER. Except for emergency or mobile equipment, a-c power supplies are
generally used. The a-c potential is rectified and filtered to obtain direct current having
the requisite freedom from ripple.
TYPES OF RECTIFIERS. Selenium or copper oxide rectifiers are frequently used to
obtain the relatively low voltages required for bias or for the plate circuits of low power
tubes. For high-voltage plate supplies, rectifier tubes are employed. These may be of
several types. The most common are vacuum tubes having a hot cathode emitter and a
cold plate. To neutralize the space-charge drop, a small quantity of mercury or one of
the inert gases is introduced into the tube. Other types of rectifier tubes use a pool of
mercury as the cathode. Electron emission is obtained, either by maintaining an electron
discharge from a hot spot on the surface of the pool by means of an auxiliary electrode
excited by a separate power source or by discharging a heavy current through a concen-
trated point on the surface of the mercury by means of an electrode which just touches
the surface of the mercury. The first of these two types of tubes has been called the pool-
type, mercury-arc rectifier; the second is known as the Ignitron. The pool-type tube is
available for single- or multiphase operation, whereas the Ignitron is commonly a single
rectifier unit and a number are connected in groups for multiphase operation. The steel-
tank mercury-arc rectifier has been frequently used for high-power applications such as
railway power supplies. It has also been used to a considerable extent in Europe as a
source of high voltage for radio transmitters. Because of its relatively high cost and the
necessity for the provision of considerable auxiliary equipment, it has not been widely
used in radio transmitters in the United States.
7-110 VACUUM-TUBE CIECUIT ELEMENTS
25. RECTIFIER CIRCUITS
Figure 4 shows the common rectifier circuits for Kenotron and mercury-vapor tube
type rectifiers with their voltage and current conditions. In calculating the d-c output
voltage, from the "E average" given for the circuits shown, the voltage drop across the
filter choke and the tube drop should be subtracted from E average to arrive at the d-c
output voltage. The relations hold if a filter choke large enough to insure a constant load
current is assumed. In practice, such a choke is usually required to obtain adequate ripple
attenuation. Eectifier tubes and steel-tank rectifiers are rated on the basis of the max-
imum average plate current they can carry, 'the duration of the cycle over which the plate
current flows, and the total voltage to which the tube is subjected during the period when
it is not passing current. This voltage is known as the peak inverse voltage. In the hot-
cathode, mercury-vapor tube, the safe peak plate current is also given, since, owing to the
low internal tuba drop, dangerously high currents may be passed through the tube, result-
ing in rapid deterioration of the filaments.
DOUBLE OUTPUT RECTIFIERS. In many transmitter applications it is desirable
to provide two plate voltages, one for the low power stages and the other for the output
amplifiers. If a single rectifier is to be used, the low voltages may be obtained by means of
dropping resistors. However, if they are equal to or less than one-half the rectifier output
voltage, one of the rectifier circuits which permits obtaining half- voltage is more economi-
cal. The single-phase bridge circuit or the three-phase full-wave circuit shown in Fig. 4,
columns 2 and 5 respectively, may be so used. Half-voltage is obtained from a center tap
on the secondary of the plate transformer in the single-phase full-wave circuit, or from
the center of the wye-connected secondaries in tjie three-phase full-wave circuit. The
additional transformer kHovolt-amperes required for the half-voltage loads can be com-
puted by considering the equivalent rectifier circuits, which are the center-tapped circuit
shown in column 1 for the single-phase rectifier or the three-phase half-wave circuit shown
in column 3 for the three-phase rectifier. If the amplitude of the current to be supplied
at half-voltage is an appreciable part of the total, a d-c component of current is produced
in the secondaries of the high-voltage transformers, in the three-phase rectifier, which
may seriously affect their operation. The effect of the d-c component may be eliminated
by using a two-winding secondary for each phase of the wye, connected in broken star.
It is generally desirable to use separate niters for the two voltage outputs in this type of
rectifier; otherwise objectionable interaction may result, causing higher ripple voltage
output than anticipated, or low-frequency feedback oscillation.
HIGH-VOLTAGE TRANSFORMERS. Transformers used in rectifier service are spe-
cially designed (see Section 6, article 14), since the insulation requirements and heating
effects are quite different from those experienced in a-c circuit practice. Secondary wind-
ing insulation will depend on the type of rectifier circuit used. In the single-phase center-
tapped secondary circuit shown in column 1, for instance, the center tap of the secondary
winding is usually at substantially ground potential, whereas in the single-phase full-wave
circuit shown in column 2 the midpoint of the secondary winding is at a potential equal
to half the d-c voltage developed by the rectifier. Fault conditions will also seriously
affect the insulation requirement of the transformer. In any of the circuits in which the
center tap or midpoint of the wye of the transformer secondaries is connected to ground
through the filter choke, a short-circuit fault will momentarily cause the full d-c voltage
to be developed across the filter choke, raising the potential of the center point of the
transformer secondaries to the full d-c voltage above ground.
Transformers for three-phase rectifier circuits may be constructed as a single three-
phase unit, or three separate single-phase transformers may be used. The first cost of
the unit transformer will generally be lower, but having three single-phase transformers
permits temporary operation in an open delta circuit if one transformer fails. Trans-
formers may be obtained for rectifiers rated up to several hundred kilowatts and up to
10,000 to 15,000 volts d-c output, in either the dry or oil-filled types. Oil-filled trans-
formers for any power are available, filled with Transil oil or one of the non-inflammable
oils sold trader various trade names, such as Pyranol or Dykanol. The non-inflammable
oils require special transformer designs, since they will attack some of the insulation
materials ordinarily used. In installations subject to the rules of the insurance under-
wifcers, it is usually necessary that transformers filled with inflammable insulating oil
be Jammted in separate fireproof vaults provided with oil sumps and drains. The size
<*f the transformer for which such protection must be provided is determined by its oil
eontenfc sad varies in the different states. Local codes should be checked.
FILTER DESIGN. The design of the filter depends largely on the service for which
tin© transmitter is to be used. Telegraph-transmitter filters are designed to the require-
RECTIFIER CIRCUITS
7-111
-H
o
O
eo
COO3
H
+ 1
p
'6
9
COCO
CO CD
+ 1
O W |M
7-112 VACUUM-TUBE CIRCUIT ELEMENTS
ment that the load current may vary at a rate corresponding to the telegraph characters,
while the filters for telephone transmitters must, usually, be capable of supplying power
at a very low audio frequency. It is usually necessary first to design the filter to secure
the desired ratio between the load voltage and ripple voltage and then determine whether
it fulfils other requirements.
Let F be the principal ripple frequency. Then F = supply frequency times number of
rectifier phases. Let xc = filter capacitive reactance; XL = filter inductive reactance;
C — filter capacitance in microfarads, and L » filter inductance in henrys.
Single stage:
Per cent ripple = (1)
XL — xc
Double stage:
Per cent ripple = 7 r« (2)
(XL — xcr
where xc and XL are the capacitive and inductive reactances, respectively, of each of two
similar stages; m = 70 for single-phase full-wave rectifier, 24 for a three-phase half-wave
rectifier, and 5 for a three-phase full-wave rectifier.
Most Economical Filter Design. A single-stage filter is more economical than the
double-stage type unless an unusually large reduction in ripple is desired, or the frequency
is low, or low filter choke reactance is necessary, as for a telegraph transmitter.
Inductance-capacitance Ratio. The ratio between filter inductance and capacitance
depends on a number of factors. If no other requirements are imposed on the filter than
ripple reduction, the most economical ratio of L to C may readily be calculated. Ordi-
narily, however, the LC ratio is fixed by other considerations. If the rectifier tubes are
worked near their current rating, the extra current flowing through the tube due to the
impedance of the filter should be checked to determine whether the total tube current is
excessive. This component of tube current may be calculated as follows :
rms ripple voltage
r ... f^
XL — xc
Filter for Telephone Transmitter. In most telephone transmitters the filter must
supply an audio component of power, since the time lag through the filter and transformer
reactances is too great to permit the audio component to be drawn directly from the trans-
former. The frequency and amplitude of the audio component depend on the type of
modulation. The relations for the various systems are given below:
1. Class B Audio: Rectifier is required to supply an audio component having a peak
value equal to the difference between the no-signal and maximum instantaneous signal
plate currents of the class B stage at a rate corresponding to twice the lowest transmitted
audio frequency.
2. Linear Amplifier and Grid-bias-modulated Amplifier: Rectifier is required to supply
an audio component having a peak value equal to the unmodulated plate current multi-
plied by the modulation factor.
3. Constant-current: No audio component exists in the d-c power source.
It will be seen from the above considerations that the linear amplifier and the grid-bias-
modulated amplifier impose the severest restrictions on filter design, while the constant-
current system requires the filter to supply no audio-frequency power. The class B
modulator requires some audio power, but the facts that the lowest audio frequency
existing in the filter is twice the lowest modulating frequency and, further, that the class C
modulated amplifier is usually supplied from the same source, drawing a steady current in-
dependent of the modulation frequency, make the filter design somewhat easier in this
case.
Linear Amplifier. If we assume a linear amplifier, completely modulated, and it is
desired to find a suitable filter combination, the following method may be used
(if r* > L/C}: Let F0 = resonant frequency of L and C; Fd » frequency at which* distor-
tion begins; F = any audio frequency, to be investigated; K « ratio of load voltage at
peak of audio cycle to unmodulated load voltage; K$ = above ratio at frequency F<z; r =
load resistance; L = filter inductance; and C = filter capacitance. Then
K = IT^fT (4)
RECTIFIER CIRCUITS 7-113
L ^ W -
r ZvFFfK
Fd « FQVKd + 1 (6)
K* = 1 - ^ (7)
Sample Calculation. Assume that a linear amplifier requires an output of 10 kw at 15,000 volts-
A filter consisting of a 15-henry inductance and 7.5-pf capacitor is provided. Determine the resonant
frequency of the filter, the value of K at 30 cycles, the frequency at which distortion begins, and K at
that frequency.
= 15 cycles per second
L = 15 henrys
C - 7.5 id = 7.5 X 10~6 farad
6.28\/15 X 7.5 X 10~6
F = 30 cycles per second
a = jp02 - F2 « 225 - 900 - -675
47r2F2Fo*L2 = 4 X 9.85 X 900 X 50,600 X 225
r2 506,000,000
K = ~675 - -0.999
V465.000 + 797
^ = i-4-
506.000,000 X 7.5 X 10
Fd = 15V0.99605 +1 =21.2 cycles per second
Thus, it will be seen that, at 30 cycles, the reduction in rectifier voltage at the peak of the audio cycle
is only 0.1 per cent, and distortion due to the filter circuit will not be encountered at any frequency
above 21.2 cycles. At this frequency the reduction in voltage is 0.395 per cent.
Class B Modulator. The same method of calculation may be followed for a class B
modulator, except that some allowance should be made for the steady d-c component of
plate current supplying the no-signal plate current for the modulator and the modulated
r-f amplifier. An approximate method is to find K as above and then to find the actual
ratio, use the equation K' = 2 — /(I — K} — K, where Kf is the ratio of load voltage at
the crest of an audio cycle to the unmodulated load voltage, corrected for the unmodu-
lated component of plate current representing the sum of the class C amplifier plate cur-
rent and the no-signal plate current of the modulator; / is the ratio of peak load current
to load current without modulation; and K is calculated in the same manner as for a
linear amplifier. It must also be remembered that only the double frequency component
of the modulating frequency appears in the rectifier circuit, and so the modulating
frequency should be doubled when it is used to evaluate FQ, F<f, and F.
Filter Chokes. Methods of calculation of the inductance required for the filter choke
are cove-red in the section on filters. In addition to inductance, it is necessary to specify the
voltage insulation or type of construction, the d-c current, and the a-c voltage. In normal
operation the full ripple voltage of the rectifier will appear across the terminals of the
choke. Its winding insulation must, therefore, be sufficient to withstand this voltage.
In addition, a short circuit in the load will subject the choke to the full d-c rectifier output
voltage, so that it must be designed to withstand this strain. The voltage insulation re-
quired between winding and core for normal operation will be lowest if the choke is con-
nected between the rectifier and ground. This does not, of course, eliminate the necessity
for the provision of adequate insulation to take care of load short-circuit.
Rectifier-tube Operation. The hot-cathode mercury-vapor tube is used in the majority
of high-voltage rectifiers for radio transmitters. In addition to the limits of peak inverse
voltage, and peak and average current set up in the rating of each of these types of tubes,
it is also necessary that the condensed mercury temperature be maintained within specified
limits. For operation of the tubes at their maximum rated peak inverse voltage, it is
usually necessary to keep the condensed mercury temperature between the limits of 20
and 60 deg cent. For temperature ranges extending from 10 to 70 deg cent, the maximum
peak inverse voltage is frequently halved. To control the condensed mercury tempera-
7-114 VACUUM-TUBE CIRCUIT ELEMENTS
ture a jet of air is directed against a spot on the lower edge of the glass bulb, and the
temperature of this air stream is occasionally controlled by means of auxiliary heaters.
It is sometimes desirable to secure additional current capacity by connecting rectifier
tubes in parallel. Because of the peculiar conduction characteristics of gases, unless such
tubes are identical the one in which the gas is ionized first will conduct all the current and
the other will not break down. This condition may be corrected by connecting a small
center-tapped choke between the two tubes or by connecting a resistance in series with
each tube so that sufficient potential is available to break down the second tube after the
first one has started conducting.
TUBE HEATER DELAY. Most of the hot-cathode mercury-vapor tubes use highly
efficient shielded cathods or filaments in order to reduce the filament power to a minimum.
Such cathodes require some time to come up to their operating temperature, and it is
usually advisable to provide a time-delay relay to prevent the accidental application of
plate voltage before the cathode has reached its operating temperature. For the same
reason, and to prevent the adherence of any particles of mercury to the anode or cathode,
each new tube should be baked out thoroughly before plate potential is applied, and then
reduced plate voltage should be applied, slowly working up to the normal operating plate
voltage. Unless these precautions are followed, severe arc-backs may result and the tube
will be permanently damaged.
TUBE-FAILXTRB PREDICTION. Mercury-vapor rectifier tubes almost always fail
by arcing back, that is, becoming conductive to a voltage of either sign. This condition
will occur, momentarily, and then clear itself; however, as the tube ages, it happens with
increasing frequency, until it cannot be tolerated, and the tube must be replaced. Each
arc-back short-circuits the plate transformer and usually trips the a-c overcurrent relays.
If a bank of tubes is used in a multiphase rectifier it is difficult to determine by visual
observation which tube has arced back. Devices which will register the flow of reverse
current, such as polarized magnetic drops, are sometimes used as indicators. However,
the short-circuit current is often so great that it will cause the indicators to drop on other
tubes as well as on the defective one. It is possible to predict with fair accuracy the time
when a tube may be expected to fail by making a routine check of the arc-drop voltage
when the tube is carrying rated current. When, on successive readings, separated by
perhaps 100 hours of normal operation, the arc drop is found to be rising rapidly, the
tube will probably soon fail and should be removed from service. These tests must, of
course, be made by removing the tube from its operating position, and applying the necessary
test voltage, which need not be greater than 100 wits.
RECTIFIER CONTROL SYSTEMS. Since high-power rectifiers must usually be de-
signed to have low regulation, a fault, in the form of either a short circuit in the load or an
arc-back in a rectifier tube or tank, may result in dangerously high currents in the system.
To minimize any trouble resulting from this source, a high-speed breaker should be pro-
vided in the power transformer primary. The breaker should be controlled by a-c over-
load relays in each phase of the primary and by a d-c overload relay in the output circuit.
If a short circuit should occur in the transmitter, the energy stored in the filter will be
dissipated in the fault even though the primary circuit is cleared instantly. For this
reason it is advisable to incorporate some series resistance in the load circuit to aid in
dissipating the filter energy. A resistor of 1 to 5 per cent of the load resistance can usually
be added with no bad effects. It should be remembered, in designing such a resistor, that
for a gassy tube or similar fault the load resistance is virtually zero, and all the rectifier
voltage will, for an instant at least, appear across the protective resistor. This should
h'ave sufficient thermal capacity to dissipate several times the energy stored in the filter
and should be insulated to cany the full rectifier voltage across its terminals. As a further
protection against high voltages across the power transformer secondary in the event of
an arc-back, it is advisable to connect a spark gap in series with a current-limiting resistor
between each high-potential secondary terminal and ground. The gap may take the form
of either a horn or sphere gap and should be set to break down at about 1.5 times the
normal voltage.
BIBLIOGRAPHY
Armstrong, R. W., Polyphase Rectification Special Connections, Proc. I.R.B., January 1931.
Lee, R., Rectifier Filter Circuits, Elec&ic J., Vol. 29, April, 1932.
Lee, R,, Radio Telegraph Keying Transients, Proc. IM,&, Vol. 22 (February 1934).
Prmce and Vogdes, If ercury Arc Rectifiers and Circuits. McGraw-Hill (1927).
RADIO RECEIVERS 7-115
RADIO RECEIVERS
By Vernon D. Landon
The functions of a radio receiver are to :
First: Select a desired signal from the heterogeneous signals picked up by the antenna.
Second: Amplify the radio-frequency signal selected.
Third: Detect the signal, thereby producing audio-frequency currents. (In the case of
continuous wave code signals, it is necessary to heterodyne the signal with a local oscillator
before detecting.)
Fourth: Amplify the audio-frequency signal.
Fifth: Reproduce the signal audibly by means of a loud speaker or headphones.
The parts of a receiver performing the above functions sometimes have overlapping
duties. For example, the antenna circuit gives some amplification due to resonance and
has some selectivity.
The simplest antenna coupling circuit is shown in Fig. 1JL, with its equivalent. ra
and Ca are the effective resistance and capacitance of the antenna, and Ls and rg are the
inductance and resistance, of a variable inductor, in the receiver. Ea is the voltage in-
duced in the antenna by the incoming signal. The step-up ratio of the circuit is denned
as the ratio of E8 to Ea. At resonance (neglecting that component of Es due to r», E8/Ea
— juLs/r, where r = r0 + r«. The step-up at a frequency other than resonance is E's/Era
= /wZ/8/z, where z — ra + rs -\- j(uLs — 1/coC).
The ratio of the step-up at resonance to that at a frequency differing from resonance
by a given amount is known as the selectance, or the discrimination ratio, for the given
frequency difference. A curve of selectance vs. frequency difference is a selectivity curve.
To a rather close approximation the selectance is equal to S = I -f- j4.TrfdL/r, where fd
measures the frequency difference from resonance. Since the only circuit constants in
this expression are L and r, the figure L/r is said to determine the selectivity of the circuit.
The selectivity is not changed by a change of carrier frequency if L/r is kept constant.
The circuit of Fig. \A has several disadvantages. The step-up is high and reasonably
constant over the tuning range, but the selectivity is poor, owing to the large antenna
resistance in series with the tuned circuit. Also it is very difficult to incorporate in a
unicontrol tuning system. The circuits of Figs. 1JE?, 1C, and ID are more commonly used.
In \B a tunable circuit is connected to the antenna through a small coupling condenser
Cc. If Cc is quite small (as it is in practice) then the antenna resistance and capacitance
may be neglected with only a slight error. By the use of Thevenin's theorem the circuit
then reduces to that on the right of Fig. IB. This is a simple series circuit. The step-up
of such a series circuit, considered by itself, is nearly a constant over the tuning range.
It is exactly constant if rs is exactly proportional to the frequency. In practice rs usually
varies slightly more rapidly than the frequency. However, in this case the input voltage
varies with frequency. As indicated in the diagram the effective driving voltage E'a
= EaCc/(C3 + Cc). Since Cs + Cc is the capacitance which produces resonance, then
C4 -f- Cc is inversely proportional to the square of the frequency. Hence E'a. is directly
proportional (and the output voltage Es is also roughly proportional) to the square of the
frequency. This is the chief disadvantage of this circuit. Its advantages are its good
selectivity and the ease with which it may be incorporated in a unicontrol tuning system.
In Fig. 1C the tunable circuit is connected to the antenna through a large inductance.
If this coupling inductance were quite large the capacitance and resistance of the antenna
could again be neglected. If the power factors of Le and -Ls are assumed to be equal a
transformation involving Th£veninjs theorem gives the equivalent circuit shown. Here,
since Ls and Le are constant, the input voltage Ea is constant. If all these assumptions
are correct and rs is proportional to the frequency, the output voltage E8 is also constant.
In practice there are three effects combining to produce a marked drooping of the step-up
at the high-frequency end of the tuning range. First, the inductance of Lc is usually not
large enough to make the antenna capacitance negligible. Hence, the effective inductance
of Lc and the antenna in series is less at low frequencies. This increases the low-frequency
step-up. Second, the distributed capacitance of Le increases its effective inductance
most at high frequencies and lowers the high-frequency step-up. Third, the resistance of
T8 usually varies faster than the first power of the frequency, lowering the high-frequency
step-up. .
An antenna circuit which is often used involves a combination of capacitative and in-
ductive coupling in order to obtain a flat step-up characteristic. This circuit is shown in
Fig. ID, with its equivalent. It may consist of a tuned secondary, of the usual type,
coupled to a primary of about eight times the secondary inductance. Loose inductive
7-116 VACUUM-TUBE CIRCUIT ELEMENTS
i
Es
T
i
E*
J
A
o
O
O.
-D-
FIG, 1. Antenna Coupling Circuits
TYPES OF RECEIVERS
7-117
coupling is used. The capacitative coupling is adjusted to the value required to give the
desired step-up at the high-frequency end of the tuning range. For uniform and max-
imum step-up it is essential that the inductive coupling have the proper phase, so that
the capacitative coupling adds rather than subtracts. To obtain this condition the
grid and antenna leads must emerge from the transformer with opposite directions of
rotation. The step-up of such a transformer is practically constant over its tuning range.
In a transformer for the broadcast band the value of the step-up usually lies between the
limits of 3 and 10, depending on design constants. If tight coupling is used giving high
step-up, the penalty is more detuning with changes in antenna constants. This results in
poor tracking, with the other tuned circuits of the receiver, unless an antenna is used of
the size for which the circuit was designed.
26. TYPES OF RECEIVERS
CRYSTAL DETECTOR RECEIVER. The simplest type of complete receiver is a
crystal detector circuit such as shown in Fig. 2. The selectivity of this receiver is very
slight, and amplification is lacking except for that due to resonance. Nevertheless local
stations can be received.
For low-impedance crystals, the selectivity of the receiver can be improved by con-
necting the input to the crystal across a portion of the coil.
FIG. 2. Crystal Detector Receiver »
FIG. 3. Regenerative Receiver
REGENERATIVE RECEIVER. Figure 3 shows the circuit of a regenerative detector.
The inductive coupling of the small coil in the plate circuit to the tuning inductance is
adjustable. When the regenerative feedback is adjusted to a critical value, just less than
that required to produce self-oscillation, a great amplification of signals results. The
selectivity curve is much too sharp, resulting in a loss of sidebands, thus unduly impairing
the fidelity of reproduction. The greatest objection to regenerative receivers is due to
their ability to oscillate when the feedback is too great. This results in a radiated signal
which produces very objectionable squeals, or beat notes, in near-by receivers. This type
of receiver is now illegal. It can be made legal by placing a neutralized stage of r-f amplifi-
cation ahead, so that it will not radiate when properly shielded.
Superregeneration of the Blocking Type. If the feedback in Fig. 3 is advanced well
beyond the point of oscillation, the oscillations become self-modulated. This is due to a
periodic blocking of the tube. The r-f voltage, rectified by the grid, produces a bias voltage
across the grid leak sufficient to produce plate current cutoff, and oscillations die out. The
charge on the grid condenser leaks off, the tube again starts to oscillate, and the blocking
cycle repeats itself. The frequency of blocking depends partly on the tube but chiefly on
the time constant of the grid leak and condenser. The higher the frequency of blocking,
the greater the feedback required to produce the effect.
When the frequency of blocking is increased to about the limit of audibility, by decreas-
ing the values of the grid leak and condenser, the circuit becomes an extremely sensitive
receiver. It is even more sensitive than the regenerative receiver, and much less critical
to adjust. The disadvantage is extremely broad tuning.
The sensitivity to weak signals is due to the fact that an oscillator cannot start oscillat-
ing in the absence of an impulse to start it. Weak impulses in the form of noise are always
present. It is only necessary for the signal to exceed the random noise in order to control
the oscillation. Since the peak amplitude of each block of oscillation is very closely the
same regardless of signal amplitude, it is difficult to see how audio-frequency signals are
produced. Probably the effect of the signal is to increase the frequency of blocking by
7-118
VACUUM-TUBE CIRCUIT ELEMENTS
Regeneration
causing oscillation to start sooner each blocking cycle. This decreases the plate current,
since the tube is cut off a greater percentage of the time.^ Thus an amplitude-modulated
signal produces audio-frequency currents, of the modulation frequency.
Superregeneration Employing One Tube Oscillating at Two Frequencies. Improved
results over the above can be obtained with the circuit of Fig. 4. The tube of this circuit
oscillates continuously at the
- Choke quench frequency of about 15 kc,
drawing grid current at one point
in each cycle. When not drawing
grid current the tube and circuit
are in a suitable condition to os-
cillate at the frequency of recep-
tion. However, when only weak
pulses or signals are present to
trigger oscillation, the voltage
does not have time to build up
to full amplitude before it is
quenched by grid current. Under
these conditions the amplitude of
the r-f voltage on the grid, when
grid current starts, is propor-
tional to the actuating
amplitude.
Fro. 4. One-tube Superregenerative Receiver
This circuit has a better signal-noise ratio than the blocking type, but it is almost
equally broad in tuning. The chief application for these circuits is for reception at very
high frequencies. For this use the broadness of tuning is frequently an advantage, help-
ing to find and hold the signal.
THE TUNED RADIO -FREQUENCY RECEIVER. A tuned r-f receiver consists of
several stages of tuned r-f amplification followed by a detector and audio amplifier.
Regeneration in Multistage Amplifiers. In a multistage tuned r-f amplifier, if capaci-
tance exists between control grid and plate, regeneration will result. In fact, coupling of
any sort between any two stages of an amplifier will result in regeneration, or oscillation,
depending on the degree of coupling.
Resistance Stabilization. Since regeneration is equivalent to adding negative resist-
ance, its effects may be largely counterbalanced, at a given frequency, by adding re-
sistance to the input circuit. This added resistance should not be placed from grid to
filament if it is desired to counteract regeneration over the whole tuning range with a
fixed value of resistance. The regeneration is much more severe at the high-frequency
end of the tuning range. Hence, it is desirable to place the added resistance in such a
position that it will have its greatest effect at high frequencies. This is accomplished by
placing the resistance in series with the grid.
^ Tlie Tuned R-f Receiver with Resistance Stabilization. Figure 5 is the schematic
circuit diagram for a complete battery-operated receiver, employing an untuned antenna
Oufput-
• B-H33
Gang Condensers Volume Control By- Pass Corvdenser
FIG. 5. Tuned R-f Receiver, Resistance Stabilized
and three r-f transformers, with resistance stabilization. Such a receiver would
e without the presence of resistors n and r2. When these resistors are given the
proper value (usually about 800 ohms) the effects of regeneration may be approximately
counterbalanced over the entire tuning range. In order to flatten the sensitivity curve
the resistors are usually made large enough to overcompensate for the regeneration at
TYPES OF BECEIVERS 7-119
high frequencies. For this reason the tuning is unduly broad at high frequencies, in this
type of receiver.
The Neutralized Receiver. Another method of eliminating oscillation is by the use of
neutralization. (See p. 7-29.) Receivers employing two and three stages of tuned
amplification with capacitance neutralization were quite popular before the development
of the screen-grid tube.
The Tuned R-f Receiver Employing Screen-grid Tubes. When screen-grid tubes are
employed in a multistage tuned amplifier, regeneration of the type discussed above is not
observed. The presence of the screen grid, between control grid and plate, reduces the grid
plate capacitance to such a low value that regeneration is appreciable only when the stage
gain is extremely high.
Nevertheless, it is necessary to take many other precautions to avoid oscillation if the
overall gain is very great.
Other Sources of Regeneration. Coupling of any sort, between any two stages of the
receiver, may give rise to serious regeneration. Coupling between adjacent stages is not
as serious as between circuits which are one or more stages removed from each other.
Capacitative, or inductive, coupling causes oscillation with equal facility because of the
change in phase obtainable by tuning the intervening circuits. Incomplete shielding of
grid and plate leads is one of the most prevalent sources of regeneration.
When the overall gain is high, the mutual inductance of the various sections of the
gang tuning condenser becomes troublesome. Owing to the use of a common rotor shaft
this coupling cannot be completely eliminated. It can be reduced to a satisfactorily low
value by careful design. It is general practice to use several wiping contacts on the rotor
shaft. The ground leads from the tuning inductances are brought separately to different
terminals on the wiping contacts, to avoid the coupling of a common ground lead.
Objectionable coupling is often caused by the use of common voltage supplies for the
cathode, screen, or plate circuits. This trouble can be eliminated by the use of small
decoupling resistors in series with the voltage supply leads for each tube and with separate
by-pass condensers.
THE SUPERHETERODYNE RECEIVER. The tuned r-f receiver requires extreme
care to avoid oscillation, because of the high overall gain required at radio frequency.
To avoid this the superheterodyne type of receiver, in which unduly high gain is not
required at any frequency, is used. Part of the required amplification is obtained at the
radio frequency and part at an intermediate frequency. This makes stabilization rela-
tively easy.
The essential idea of the superheterodyne receiver is to amplify all signals at the same
fixed frequency. The essential component parts are the preselector, the frequency con-
verter, the intermediate-frequency amplifier, the audio amplifier, and the loud speaker.
A typical receiver of this type is shown in Fig. 6.
The Preselector. The preselector consists of an antenna input circuit with, or without,
one or more tuned r-f amplifier stages.
The operating characteristics of the preselector are identical with those of corresponding
units in a tuned r-f receiver.
The preselector assists in producing discrimination against signals on adjacent fre-
quencies, but the intermediate-frequency amplifier is so much more effective for this
purpose that the use of the preselector is not warranted for this alone. Its essential func-
tion is the elimination of undesired responses at frequencies widely different from that of
resonance.
The Frequency Converter. Frequency conversion is obtained by the use of the first
detector and oscillator. In most receivers, the oscillator operates at a frequency higher
than the signal frequency. The difference in frequency is the intermediate frequency.
Voltage from the oscillator and from the signal is fed to the first detector, and the output
is amplified in the i-f amplifier. Previous to 1933, a majority of receivers employed sep-
arate tubes for the oscillator and first detector, usually using a circuit in which the oscilla-
tor voltage was fed to the first detector cathode. A majority of modern receivers employ
a single tube in which the two functions are combined. An example of this type of tube is
the 2A7, used in the circuit of Fig. 6.
Combined First Detector and Oscillator. In the 2A7 tube the first two grids, adjacent
to the cathode, comprise the oscillator elements. The voltage fluctuations of the first grid
control the electron stream, not only to the oscillator plate (called second grid for con-
venience although it includes only two vertical rods) , but also that to the remainder of the
elements. The current arriving at the output plate of the tube consists of pulses, at the
frequency of the oscillator. The amplitude of these pulses may be varied by the control
grid. The remaining grid, or screen, acts as a shield between the oscillator elements and
the control grid and output plate. It also screens the control grid from the output plate.
7-120
VACUUM-TUBE CIRCUIT ELEMENTS
TYPES OP RECBIVEES
7-121
The component at the difference between oscillator and signal frequency corresponds
to the intermediate frequency; it is selected and amplified by the i-f amplifier.
Tracking. One of the most important problems of superheterodyne design is tuning
the oscillator and the preselectors with a gang tuning condenser. The problem is to main-
tain the oscillator at a uniformly higher frequency than the preselector, as the preselector
is tuned over the frequency band. The frequency difference must remain equal to the
intermediate frequency. Since the oscillator is operated at a higher frequency than the
preselector, it has a tendency to change frequency too rapidly.
One method of correcting this is to specially shape the rotor plate of the tuning con-
denser which is used in the oscillator section of the gang tuning condenser. Another
method is by means of fixed condensers in series and shunt with the oscillator tuning
condenser. These reduce the rate of change of frequency. When the two auxiliary con-
densers and the oscillator inductance have the proper value, the oscillator frequency
deviates only slightly from that desired, as shown in Fig. 7.
w
<Sr
_$_
V
14.00
1800
l&OO
\
\
\
1100 1000 900 800
ri^yca.esjier Second
FIG. 7. Oscillator Tracking under Ideal Conditions
700
600 550
Figure 8 is a curve which is useful in deterrnining the proper values for the oscillator
inductance and the capacitances to obtain the best tracking with the preselector. In the
curve: a is the ratio of oscillator tuning inductance to tbe secondary inductance of the
r-f transformer; Ca is the value of the oscillator series condenser; C/ is the difference be-
tween the oscillator trimmer capacitance and the r-f transformer trimmer capacitance.
Values of Cs, Cf, and a are plotted against intermediate frequency. The lower abscissa
scale is used, assuming that the range to be covered is 550 to 1500 kc. For other ranges the
upper abscissa scale should be used. The curve is for the condition of 400 ju/zf total circuit
capacitance at the low-frequency end of the range. If the maximum capacitance is
changed, Cs and Cf change in the same ratio, while a remains unchanged.
The Intermediate-frequency Amplifier. The i-f amplifier consists of one or more stages
of amplification following the first detector. The tuning is fixed at the intermediate
frequency. Usually two coupled circuits are used in each i-f transformer. The frequency
chosen usually lies between 100 and 500 kc per sec. High gain and good selectivity are
easily obtained at these frequencies, particularly towards the lower of the two values.
The Diode Pentode Tube. In the circuit of Fig. 6, the fourth tube is a combination
of a diode and a pentode in a common envelope. The diode and pentode together serve as
7-122
VACUUM-TUBE CIRCUIT ELEMENTS
detector and audio amplifier. This combination tube may replace two separate tubes in
all circuits except those requiring different d-c cathode potentials.
Undesired Responses. Although the superheterodyne has many advantages, it is sub-
Sect to a number of undesired responses and interfering beat notes which do not occur
in a tuned r-f receiver. However, careful design minimizes these difficulties.
The Image Response. The most important undesired response in a superheterodyne
is known as the "image." As explained above, the intermediate frequency is the difference
between the signal frequency and the oscillator frequency. The oscillator is operated
above the signal frequency. However, i-f signals are produced equally, well by a beat
Intermediate Frequency
10.000 1.0 H
1
CO _
3.000 0.1 10
3.0
100 .10 1
20 3O 50 70 100 200 30O 500 700 1000 2000 3000
Lniarmediaie Frequency m Kc-
PIG. S. Proper Values of Oscillator Inductance and Capacitances for Best Tracking with the Preselector
between the oscillator and a signal which is above the oscillator in frequency. The first
detector is equally responsive to signals at either of these two frequencies. The only
means of selecting the desired (lower frequency) of these two response points and attenu-
ating the other is by means of the preselector. The higher, the frequency of the interme-
diate amplifier, the greater the frequency separation of the desired signal and the image
response; hence, the image response ratio is greater for a high intermediate frequency.
With an intermediate frequency of 175 kcr the ratio of the sensitivity at the desired response
to that at the undesired response can be made about 1000 at the high-frequency end of the
broadcast range and about 10,000 at the low-frequency end. Although higher intermediate
frequencies give higher image response ratios, other difficulties may develop from their
use, as described below.
Harmonics of the Intermediate Frequency. Another source of difficulty which may
be present in the superheterodyne is a beat note which occurs when reception is attempted
afc a frecfuency corresponding to a harmonic of the intermediate frequency. The reason
to? tills beat note is that the second detector produces these i-f harmonics. If a very small
aiaownt of coupling exists between the second detector circuit and the antenna, or the r-f
transforiBex, the i-f harmonic beats with the incoming signal producing a disagreeable
squeal
TYPES OF KECEIVERS
7-123
7-124
VACUUM-TUBE CIRCUIT ELEMENTS
The higher the order of the harmonic the less its amplitude in the detector circuit.
Hence it is easier to suppress the beat note due to higher-order harmonics than that due
to the second and third harmonics. The highest intermediate frequency which can be
used if the third harmonic is to be kept outside of the broadcast frequency band is 175
kc. This accounts for the great popularity of this figure. When higher intermediate
frequencies are used, such as 450 kc, the severity of the harmonics in the broadcast band
is increased, but the number of interference points is reduced from five to two. By very
careful shielding, the beat notes resulting from these harmonics may be almost completely
eliminated. The greatest dimculty is obtained with the second harmonic.
Other Responses. The above are the most important of the undesired responses, but
many other types occasionally give trouble. For example, two broadcasting stations may
beat together to produce i-f signals independent of the local oscillator. Harmonics of the
oscillator may beat with signals of various frequencies and with their harmonics, etc. A
good preselector is the best insurance against all these.
ALL-WAVE RECEIVERS. The popularity of short waves increased very rapidly
during 1933 and 1934. For this reason most of the commercial entertainment receivers
now include provision for the reception of frequencies other than the standard broadcast
band. Many of these receivers employ the name * 'all-wave," but this is a misnomer as
none of these receivers cover the whole r-f spectrum. The circuit of a typical receiver of
this kind is shown in Fig. 9. The circuit is entirely conventional, except that the preselec-
tor transformers and the oscillator transformers may be switched to any one of the five
bands which it covers.
The r-f transformers for the low-frequency bands are purposely designed with restricted
gain, so as to maintain approximately uniform sensitivity on all bands. This is necessary,
because the gain obtainable in a single stage is limited to a low value at high frequencies.
RECEPTION OF CONTINUOUS WAVE CODE SIGNALS. In the reception of un-
modulated code signals it is necessary to supply a local oscillator to produce an audible
beat note with the incoming signal. In the regenerative detector circuit of Fig. 3 it is only
necessary to advance the tickler to a point just beyond where oscillation starts in order
to receive this type of signal. The regenerative detector may be preceded by one or more
stages of tuned r-f amplification to increase the sensitivity.
The circuits of Figs. 5, 6, and 9 may be used to receive code signals by the addition of
an external oscillator. In the tuned r-f receiver the oscillator must be tuned to beat with
the signal directly. Hence it must be tunable over the receiving frequency range. With '
superheterodyne the lo<ial oscillator may beat with the signal at the intermediate frequency.
Hence its tuning may be fixed. The oscillator should be coupled weakly to the detector
input circuit.
TUNING INDICATORS. Because radio stations are not always modulating, it is
somewhat advantageous to have a visual indication of resonance, rather than to depend
on audio output as a check on the accuracy of timing. There are many different methods
for accomplishing this. One of the simplest is to place a milliammeter in the B supply
lead to one of the r-f amplifier tubes which is subjected to automatic volume control. The
stronger the signal, the higher the bias on this tube, and the lower its plate current. Hence
the deflection of the needle downward from its peak value at no signal is a good indication
of signal strength and of the accuracy of tuning.
1 2 5 10 20 50 100200 500 g g
^V. O CM
PIG. 10. Overload and AVC Curves
FIDELITY CHARACTEBISTICS
7-125
AUTOMATIC VOLUME CONTROL. The circuit connections for automatic volume
control are shown in Fig. 6. The diode second detector develops a d-c voltage which is so
connected as to increase the bias on the amplifier tubes with increased signal strength.
The result of this connection is that strong signals produce only slightly greater audio
response than weak ones. In Fig. 10 the audio output of a typical receiver is plotted
against signal strength for maximum, and for a reduced manual volume control setting.
A manual volume control, such as that shown in the diode circuit, is necessary to adjust
the level of sound volume. After this adjustment is made signals come in at approximately
the same volume. One of the important advantages of automatic volume control is a
reduction of the effect of fading signals.
27. FIDELITY CHARACTERISTICS
The circuits affecting the fidelity characteristics are: the r-f amplifier, the automatic
volume control circuit, the audio amplifier, the tone control, the output transformer, and
the loudspeaker. The effect
of the loudspeaker is not
included in the curve of
Fig. 11. Loudspeaker char-
acteristics are discussed in
Section 6.
The overall fidelity curve
of Fig. 11 is the product of
the fidelity curves of the
component parts of the re-
ceiver.
EFFECT OF R-F CIR-
CUITS ON FIDELITY.
The r-f circuits affect the
fidelity curve by cutting the
high-frequency response.
The modulation on a signal
consists of continuous wave
M
O
0
a40
I-
&
200 300 500700 1000
Frequency In Cycles per Second
FIG. 11. Fidelity Curves Showing Effect of Tone Control
304050 70 100 200 300 5007001000 20003000 4000
signals (called sidebands)
on frequencies adjacent
to the carrier frequency.
These sidebands differ in frequency from the carrier by the value of the modulation fre-
quency. The selectivity curve of the r-f and i-f amplifier shows quite appreciable decrease
at only 2 or 3 kc from resonance. Hence the fidelity curve indicates this same decrease of
the high audio frequencies.
THE EFFECT OF THE AUTOMATIC VOLUME CONTROL ON THE FIDELITY.
The automatic volume control reduces the effects of fading, delivering to the detector a
signal having only slight variations in amplitude, in spite of the wide fluctuations of
signal amplitude on the antenna. In a similar manner the amplitude fluctuations of the
signal, corresponding to low-frequency modulation, may be almost completely wiped out
if the action of the automatic volume control is too fast. The action of this circuit may
be slowed down by increasing the values of the resistors and by-pass condensers in the
return leads of the tuning inductances. If the action is too slow the delay becomes notice-
able to the ear. Shocks of static then blot out appreciable portions of the program, and the
change in volume when tuning in stations may be noticeably slow. For this reason the
time constant should be low enough so that there is a small but appreciable effect on the
low-frequency portion of the fidelity curve.
THE RESISTANCE-COUPLED AUDIO AMPLIFIER. In Fig. 6 the diode section
of the diode-pentode is resistance-coupled to the pentode section. Also, the pentode is
resistance-coupled to the output tube. Neglecting the slight effect of the grid leak, the
gam of a resistance-coupled amplifier is the ratio of the voltages applied to the grids of the
preceding tube and the following tube. It is equal to E^/JSi = j*r/(rp + r), where p
is the amplification factor of the tube, r is the load resistance, and rp is the plate impedance
of the tube. Or, if the plate impedance is very high, E%/Ei — smr, where sm is the trans-
conductance (or mutual conductance) of the tube at the operating voltages.
These formulas neglect shunt capacitance and the coupling capacitance. At high
frequencies the shunt (plate-filament, grid-filament, and other) capacitances affect the
r esult. The response is attenuated to 70 per cent of the mid-range value, at the frequency
7-126
VACUUM-TUBE CIRCUIT ELEMENTS
where the shunt capacitative reactance is equal to the effective resistance of r and ry in
parallel. ,
At low frequencies the coupling capacitance reduces the gain. The response drops to
70 per cent at the frequency where the reactance of the coupling capacitor is equal to the
resistance of the grid leak. The effect of the diode resistance-coupling circuit may be
calculated in a similar manner.
TONE CONTROL. The above paragraphs neglect the effect on the fidelity, oi ±C-lb
and C-24 (in Fig. 6), which constitute the tone control. At the maximum setting of the
variable resistor the effect of these two units
is very slight. However, when the control
is turned back, high frequencies are pro-
gressively attenuated. A fidelity curve at
maximum and minimum tone control setting
is given in Fig. 11.
The major use of the tone control is to
improve the apparent signal to noise ratio.
Noise is usually uniformly distributed over
the audio-frequency spectrum, while the
signal energy is chiefly contained in its
lower frequency components. Hence when
the tone control is turned back the signal is
a smaller percentage than the
input
Output
FIG. 12. Compensated Volume Control Circuit
reduced by
noise.
The tone control may also sometimes be used to improve faulty fidelity in the trans-
mitted signal.
THE EFFECT OF AUDIO TRANSFORMERS ON THE FIDELITY. Audio trans-
formers of either the interstage or output type affect the fidelity by cutting both the
Mgh- and low-frequency response. However, the degree may be largely controlled by
design. (See pp. 6-13 to 6-25.)
COMPENSATED VOLUME CONTROL. To the human ear the apparent loudness
of sound at various frequencies changes at a different rate as the amplitude of the sound
waves is changed. This makes it desirable to accentuate low frequencies and high fre-
quencies when the volume control is turned down. A circuit employed to accomplish
orvn
Percent of Response at,400*v
5 » « ft g § g }
fi,O o o <5 ooooc
1.
2.
0.
0.
10.
32
50
30
W.
w.
W.
Pow«
r Output a
1400
*v
3.
1
A'~
\
\
>
/
f
I
IV
s
/
/
s"~"
&*5
^
>ft
*f*
^
* *£,"
Volurne
^s
^<
^
(0 50 70
100 200 500
1000 2OOO 5000 10^000
Frequency In Cycles per Second
Fio. 13. Variation of Frequency Response with Setting of Compensated Volume Control
this is given in Fig. 12. Figure 13 gives the fidelity curve of a receiver incorporating this
artfait. A receiver employing compensated volume control has a more natural sound at
all -woiume levels.
HOISE SUPPRESSION. When automatic volume control is employed with a re-
cersner of high sensitivity, the receiver automatically goes to full sensitivity when tuned
between stations. The results are disagreeably strong reproduction of the static and
general isierferenee, which is always present in the background at any frequency. In
RANDOM NOISE
7-127
order to make tuning more pleasant, circuits of various types have been developed for
cutting off the audio amplifier in the absence of a signal carrier. One popular circuit for
this purpose is shown in Fig. 14.
When no signal is present, no current flows in the diode circuit. Hence, no bias voltage
is applied to the grid of T2 and maximum plate current flows through r2. The voltage
developed across r% biases V$ to cutoff so that it cannot amplify. The audio signals from
interfering noises cannot pass this point. When an r-f signal is present, current flows in
the diode circuit producing d-c and a-c voltages across the diode circuit resistor. The
FIG. 14. Noise Suppressor Circuit
d-c voltage biases Vz to cutoff. There is then no voltage drop across r%, so Vz operates
with normal bias. Vz then functions as an amplifier for the audio-frequency voltage
applied to its grid through £4.
28. RANDOM NOISE
Random noise (sometimes called fluctuation noise or Johnson noise) is a fundamental
form of interference which prevents the satisfactory reception of signals below a certain
level.
Random noise comes from two sources, thermal agitation in circuit resistances, and
shot effect in vacuum tubes. Thermal-agitation noise comes from the random motion of
electrons in a conductor due to its temperature. The open-circuit rms noise voltage across
a resistor is
En = VlKTr A/ (1)
where K = Boltzmann's constant = 1.37 X 10"53 joule per degree Kelvin.
T — absolute temperature in degrees Kelvin.
r = value of the resistance in ohms.
A/ = the effective noise bandwidth of the instrument used to measure the voltage.
Since the effects of shot noise are indistinguishable from those of thermal noise, it is
customary to measure the shot noise of a vacuum tube in terms of the equivalent noise
grid resistance. This is defined as the value of external grid resistance required to double
the noise power output of the tube over that with the grid shorted. The value for a
triode is approximately,
gm
where gm is the trans conductance of the tube. The value for a pentode is approximately
four times as high.*
Noise Factor. The "available power" of a signal generator is the power delivered to
a load resistance under the condition of an impedance match. Thus the available noise
power of a resistance considered as a noise generator is:
-^- « KT A/ (3)
K the resistance r is the impedance of a receiving antenna, and if no other noise sources
existed, then a signal noise ratio of unity would be obtained when the signal power avail-
able from the antenna was KT A/. This is the (unattainable) ideal which can never be
* B. J. Thompson, D. O. North, and W. A. Harris, Fluctuations in Space-charge-limited Currents
at Moderately High Frequencies, RCA Rev., VoL IV, No. 3 (January 1940).
7-128 VACUUM-TUBE CIECUIT ELEMENTS
improved upon. Actually other noise sources always exist, so that the signal required
for unity signal noise ratio is always greater than KT A/. The ratio by which it is greater
is called the noise factor. This ratio is usually expressed in decibels. Below 100 Me re-
ceivers can be built that have a noise factor only a few decibels above thermal. Above
600 Me, 10 db above thermal is considered good.
The test for "noise factor" is not yet accepted by the Institute of Radio Engineers as
a standard test, but its use by the armed services during World War II became so wide-
spread that its adoption as a standard seems inevitable.
The Nature of Random Koise. Random noise may be considered to be made up of
an infinite number of sinusoidal components of different frequency. The amplitude of
any single frequency component is infinitesimal, but in any finite bandwidth the rms
voltage is proportional to the square root of the bandwidth though independent of the
mean frequency.
Distribution of Amplitude. The actual voltage at any instant cannot be predicted,
but an accurate statistical prediction can be made of the fraction of the time, taken over
a long period, that the voltage will exceed any given value. This fraction of the time is
identical with the probability that the given voltage V will be exceeded at a given instant
and is equal to
where E is the rms voltage of the noise.
Distribution of Envelope Amplitude vs. Time, If the bandwidth of the circuit pass-
ing the noise is small compared to the mean frequency, then the amplitude never changes
abruptly from on© cycle to the next. Thus, in a graph of the wave, if the peaks of adjacent
cycles are connected with a smooth line the resulting line is the envelope of the wave and
is a function varying much more slowly than the wave itself. The probability that the
envelope will exceed a certain value A at any instant is
The Values of Variotis Averages.f The average absolute value of the voltage is:
F =
The mean value of the envelope is: A — 1.252.S.
The root mean square deviation of the envelope from its mean value is:
Ar » <X655# (6)
The root mean square value of the envelope is: .Anns
The most probable value of the envelope is: AP = ±E.
BIBLIOGRAPHY
Bxperimeiatal Wirdes* and Wireless Engineering,
Proc. LR-E.
Sfcarky, K. R^ Radio Receiver Design,- John Wiley (1943).
Terma®, F. ^.Radio Engineering. McGraw-Hill (1937).
Zepler, E. E,, The Technique of Radio Design. John Wiley (1943).
RADIO TRANSMITTERS
By J. E. Y<mng
A radio transmitter is defined as a device for producing r-f power for purposes of radio
1a*ansmission. It also contains means of modulating or varying that r-f power, designated
as the carrier wave, in correspondence to the intelligence it is desired to transmit. Tele-
vision transmitters or others using the pulse technique, as well as those employing fre-
$oetxry modulation, are discussed in other sections. See Sections 8, 9, and 20. This sec-
tkm will be concerned with broadcast and communications transmitters employing ampli-
t**de modulation.
, "^be Distribution of Amplitude with Time in Fluctuation Noise, Proc. I.R.E.,
. oCr-oo (February 1941).
INTERMEDIATE-RADIO-FKEQTJENCY AMPLIFIERS 7-129
NATIONAL AND INTERNATIONAL REGULATIONS. Since radio communication,
broadcast or point-to-point, involves transmission through a common medium, it has
been necessary to set up national and international rules defining the frequencies, or chan-
nels, frequency tolerance, and type of emission for all radio stations. In addition, the
Federal Communications Commission has set up national rules and standards governing
frequency assignments, transmitter power, time when testing is permitted, specifications
of performance regarding distortion, noise, and fidelity, grades of operators to be em-
ployed, etc., for all types of radio transmission. Other agencies, particularly the Radio
Manufacturers Association, have been active in setting up recommended standards of
performance and uniform methods of writing specifications and testing for various classes
of transmitters.
RADIO TRANSMITTER— SCOPE. The transmitter is usually considered to consist
of all audio equipment operating above standard telephone-practice levels, and all r-f
equipment from the source of the r-f oscillations to the transmission line connecting the
transmitter to the antenna. Within the equipment defined by these limits is contained
sufficient audio-frequency amplification to raise the input signal to a level high enough to
perform the function of modulation, r-f amplification and multiplication to raise the
power level and frequency of the r-f oscillations to the output level, and the necessary
power supplies for these circuits. The function and application of vacuum tubes to these
elements of the radio transmitter are discussed in other articles of this section; only cer-
tain general aspects of design and performance will be covered here.
FREQUENCY CONTROL. The requirements of frequency stability are virtually
always too severe to permit modulating (including c-w keying) an oscillator used as a
direct source of antenna power. The usual practice is to use a low-power oscillator, sep-
arated from the modulated amplifier by a sufficient number of stages to prevent interac-
tion caused by changes in impedance of the modulated stage resulting from the processes
of modulation or other variations in load.
For transmitters operating on fixed frequencies, quartz crystals are commonly used as
the frequency-deterrnining element. A frequency stability of 10 parts per million is quite
easily achieved with a quartz-crystal-controlled oscillator in which the temperature of
the quartz plate is not permitted to vary more than ±1 deg cent.
Some types of transmitters, particularly those used for military applications, operate
on frequencies which may frequently be changed. For these applications quartz crystals
are not practical and a master oscillator in which the tuned circuit is the frequency-de-
termining element is employed. Such oscillators, having as much as 2 : 1 frequency
range, may be designed to have a frequency stability better than 1 part in 10,000 for
moderate variations of temperature, humidity, and power supply voltages.
OSCILLATOR POWER. It is possible to design crystal-controlled oscillators which
will produce several hundred watts of output power; however, such oscillators are difficult
to adjust and somewhat less stable than those of lower power output. It is better design
practice to use a crystal oscillator which has only a few watts of output, followed by high-
gain shielded-grid amplifiers, to achieve maximum frequency stability, and, in keyed-
oscillator circuits, freedom from chirps and frequency creepage. This practice also per-
mits the use of small crystals mounted in compact holders, since the crystal dissipates
very little heat.
29. mTEMvIEDIATE-RADIO-FREQT3ENCY AMPLIFIERS
The intermediate-r-f amplifier stages perform the triple function of increasing the power
level of the frequency-controlled oscillator, multiplying its frequency, if required, and
acting as a buffer between the modulated amplifier and the oscillator. In the interest of
simplicity, intermediate amplifier stages usually employ high-gain, multigrid tubes so that
it is not uncommon to attain all three of these objectives with one or two intermediate
amplifier stages. In high-level modulated and telegraph transmitters the intermediate
amplifiers are operated class C. In low-level modulated transmitters the intermediate
amplifier stages following the modulated stage must reproduce the audio-modulated
envelope and must, therefore, be operated as class B r-f amplifiers. (See p. 7-22.)
INTERSTAGE COUPLING CIRCUITS. Amplitude-modulated transmitters are rarely
used at frequencies above 40 Me. Up to this frequency no special precautions are ordi-
narily required in interstage circuits. In general, it is desirable to make the circuits as
simple as possible to avoid dangerous multiple resonances and parasitics. Typical coup-
ling circuits for shielded-grid tubes are shown in Fig. 1. Note that the grid leak is not
by-passed and that grid and plate feed circuits are dissimilar. It frequently happens
that the input resistance of the driven amplifier is so low that the r-f choke in series with
7-130
VACUUM-TUBE CIRCUIT ELEMENTS
the grid leak may be eliminated without appreciably affecting the driver power output.
This should always be done where calculations so indicate, since a possible parasitic circuit
is thereby eliminated. For the same reason it is desirable to use the voltage obtained by
the now of rectified grid current through a resistor as grid bias rather than to obtain this
voltage from a separate source. Protection against excessive plate dissipation, if the
excitation fails, may be obtained by the use of sufficient cathode bias.
1
•4-B -C
rttJL. \\
Ib j
^ 1 -
i
h
Ib
I e tf
NCj 1 -?
-s
^2
j n
\ °i '
C2'
\ IT
FT
+ B -C
Eia. 1. Interstage Coupling Circuits
CIRCUIT 0, or KVA/KW RATIO. Unmodulated intermediate amplifier stages are
not critical with respect to interstage coupling circuit Q, although it is desirable that the
circuit, looking from the grid of the driven tube, be of high enough Q to insure sinusoidal
wave shape in spite of the variable-impedance characteristic of the grid, as it is driven
positive. Unfortunately, in the grounded filament circuits, the voltage relations are such
that the driving tube puts energy into the coupling circuit almost 180° away from the
time when it is absorbed by the grid of the driven amplifier. The energy storage must be
sufficient to take care of this condition. The wave shape will be adequate if the circuit
Q is greater than 10, unless the driven tube grid impedance at the peak of the positive
grid swing is extraordinarily low. Unless the driving stage is modulated, even higher
values of Q are useful and desirable, provided the concomittant coupling circuit losses are
not thereby made excessive,
HARMONIC AMPLIFIERS. Because of special considerations, such as crystal ac-
tivity, stability, etc., frequency multiplication is ordinarily employed where the carrier
frequency is higher than 10 Me, The necessary multiplication is accomplished in the inter-
mediate amplifier stages. The multiplication through any one amplifier stage may be
from twice to as high as five times. The plate efficiency of the amplifier tube is very
neiyriy inversely proportional to the order of multiplication, if the most favorable condi-
tions of loading and open angle of plate current are chosen for each multiplication. Be-
cause of the relatively low efficiency obtained when multiplying five times, this amount of
multiplication is rarely used in any one stage. Because of the generally poorer plate-circuit
©ffiekaaey, multiplication is usually accomplished at low power level, followed by amplifiers
tuafed to the output frequency, to boost the power level as required.
POWER AMPLIFIERS
7-131
Optimum Angle of Current Flow. The term "angle of current flow" represents the
portion of the grid voltage cycle during which plate current flows, expressed in degrees.
The optimum angle of current flow depends on how nearly the plate-current plate-voltage
characteristic conforms to the 3/2 relation, and for a 3/2 characteristic may be shown to be
approximately 130° to develop maximum second-harmonic voltage in the plate circuit,
85° for the third, 65° for the fourth, and 50° for the fifth. The angle of current flow is
given by the relation cos — = ~ , where 6 is the angle of current flow in degrees
of the excitation frequency, Ec is the grid bias, E0 the projected cutoff bias, and Eg the
grid excitation voltage. Negative bias voltages should be written in as negative numbers.
Calculation will show that an open angle of 60° may be obtained with a bias voltage of
not less than ten tunes cutoff bias. As the open angle is further restricted, the required
bias voltage increases rapidly. It is not usually economical to use an open angle of plate
current flow of less than 60° or to attempt to raise the frequency more than four times
through a single amplifier stage. This does not hold true where the output power required
is small, as in frequency-measurement work, where only milliwatts of power are usually
required, and where the frequency may be multiplied many times,
30. POWER AMPLIFIERS
Power amplifiers may be either grid- or plate-circuit modulated. (See Modulators,
pp. 7-73 and 7-74.) If the former, the power amplifier must be so operated as to reproduce
accurately in its plate circuit an r-f envelope having the same wave shape as that of the
excitation voltage. This may be accomplished by using either a linear amplifier or a
Shunt neutralizing
HI—
Plate
tuning
Loading
+dc
FIG. 2.
Typical R-f Amplifier
high-efficiency Doherty amplifier. The latter circuit utilizes linear amplifiers in pairs
and provides for dynamic changes in drive and loading so that the average plate-circuit
efficiency is several times that which may be obtained with a conventional amplifier.
Two circuit paths are provided; in the first, the amplifier tube is adjusted to operate at
the upper knee of its dynamic characteristic. Between its plate circuit and the load is
connected a 90° phase-shifting network. The second tube is biased so that its plate cur-
rent is almost zero under carrier conditions. As the drive increases during the positive
excursions of the modulation cycle, the plate current of this tube, and its power output,
increase in the same manner as an overbiased linear amplifier. The effective load resist-
ance seen at the output of the 90° network connected in the plate circuit of the first tube
increases as the second tube supplies power to the load. Because of the familiar impedance
characteristic of the 90° network, this results in a reduction in resistance at the input
terminals of this network. Therefore, the effective load resistance of the first amplifier is
reduced and its power output is proportionately increased. Thus, at the peak of the
positive excursion of the driving voltage, the power output of the first tube is doubled,
because of its increased loading, and the output of the second tube is increased in the
familiar fashion of a linear amplifier, so that it is also twice the carrier output. The total
power output of the amplifier is thus four times the carrier level, fulfilling the condition
for 100 per cent upward modulation. On the downward excursion of the modulation
cycle the second amplifier is biased off completely, and the first amplifier functions as a
conventional linear amplifier.
7-132
VACUUM-TUBE CIRCUIT ELEMENTS
The envelope wave-form distortion resulting from the use of the Doherty amplifier is
usually too great to be tolerable in high-fidelity systems. This defect may be remedied
by applying overall feedback from the output terminals of the amplifier, through an r-f
rectifier back into the audio-frequency amplifier circuits at some convenient point.
> Amplifiers employing plate-circuit modulation are termed "high level." In practice
the amplifier is operated class C, and the energy to perform the modulation function is
provided by a class B modulator. (See Modulators, p. 7-74.) _ High-level amplifier
output circuits must provide the necessary impedance transformation between the plate
circuit of the tubes and the load and in addition must provide sufficient r-f harmonic at-
tenuation to prevent excessive harmonic radiation. In practice, the Q of the output tank
circuit is generally made quite low, from 4 to 8 for single-ended amplifiers, and additional
harmonic attenuation is obtained, if necessary, by a low-pass filter inserted between the
terminals of the amplifier and its load. A typical amplifier circuit employing shunt neu-
tralization is shown in Fig. 2.
The high-level, modulated amplifier has the advantage that it is simple to adjust and
uncritical in its operation. In addition, its quiescent (carrier level) efficiency is very high.
Since the average percentage of modulation rarely exceeds 15 per cent in broadcast
operation, the quiescent efficiency is a most important consideration in the economics of
transmitter operation.
R-F HARMONIC RADIATION". Under the present conditions of crowded frequency
assignments throughout the r-f spectrum, the first few multiples of the transmitter fre-
quency— the frequencies that contain most of the harmonic energy — will often interfere
» furvdemental frequency
harmonic frequency
FIG. 3. Harmonic Attenuator
with some other radio service. Thus, because of a particular interference problem, one
harmonic often must be reduced far more than the rest. The problem should first be
analyzed, by making measurements to ascertain definitely that the interfering signal re-
sults from direct radiation from the station or its antenna. It frequently happens that a
wire or metal surface located near the point of interference, or even the receiving antenna
itself, is picking up energy from the transmitter and through the agency of an oxide-
covered joint is itself producing the harmonic signal. This may be checked by field-in-
tensity measurements made at a series of points on a line from the transmitter to the
point of interference. Peaks in the harmonic signal intensity will be observed in the vicinity
of such harmonic generators. The remedy is obvious but not always simple. Very often,
however, a single guywire or other metal object having dimensions comparable to the
wavelength in question will be found to be the source of the interfering signal.
Tbe field-intensity meter may also be used to determine whether the interfering har-
monic is radiated from the transmitter directly or from the transmitting antenna if the
two are sufficiently separated so that a directional fix may be obtained. If the radiation
ajppears to be from ihe antenna, the signal energy may be carried by the transmission
tee from the transmitter to the antenna, or it may again result from rectification either
«fc m oxidized metal joint or at a tube rectifier, such as is used for remote antenna cur-
raisfc leading or feedback. If the antenna rectifier is the offender the trouble may be cured
gr eonaeetog a Jew-pass filter, designed to cut off just above the transmitter frequency,
^reea t&e rectifier and the point where it picks up its energy from the transmitter
output.
POWER AMPLIFIERS 7-133
If the interfering signal emanates from the transmitter and is carried to the antenna by
the transmission line, a trap, consisting of a circuit parallel-resonant to the harmonic, in
series with the transmission line, and a circuit series-resonant to the harmonic in shunt
with the line, will usually result in sufficient attenuation to eliminate the interference.
Such a circuit may be designed so that its insertion will not affect the transmitter per-
formance at its fundamental frequency, and it is preferably constructed so that the tuning
of at least the shunt arm is variable, to permit exact adjustment to the harmonic fre-
quency. Figure 3 shows one typical circuit.
If a balanced transmission line is used, the trap circuits should be symmetrical, with
their center taps grounded to prevent in-phase transmission of the harmonic along the
transmission line wires.
If the directional fix indicates that the transmitter itself is radiating the interfering
signal, it may be necessary to resort to complete shielding to eliminate the trouble. More
frequently, sufficient improvement will be obtained by other minor design changes, such
as better grounding, more direct return of plate tank lead to filament of power amplifier
or elimination of stray capacitance coupling between plate and output connection.
NEGATIVE FEEDBACK. The distortion, noise, and frequency characteristics of a
telephone transmitter may be considerably improved by the application of negative feed-
back over all or part of the system. Two general methods of use of negative feedback
are common. In transmitters using low-level modulation, followed by linear amplifiers,
feedback voltage is derived from an r-f rectifier coupled to the output of the power am-
plifier. This signal, of the proper amplitude to secure the desired feedback, is introduced
into one of the audio-frequency amplifier stages. Since the r-f rectifier is in the 0 loop of
the feedback circuit, noise or distortion generated hi it will appear in the ouput of the
transmitter. It must, therefore, be carefully designed to reproduce accurately the audio
envelope of the output r-f signal.
One difficulty frequently encountered in the application of this type of feedback to
broadcast transmitters is that the transmitter antenna also functions as a receiving an-
tenna for signals from other broadcast stations. Sufficient voltage may be developed
in the circuit to which the feedback rectifier is connected by another broadcasting station,
located in the immediate vicinity, to generate a series of cross-modulation products in
the rectifier. Any of these new frequencies lying within the pass band of the a and |8
loops of the audio system will produce sidebands which will be radiated by the antenna
and may cause serious interference. Such effects may be greatly reduced by installing
a trap tuned to the frequency of the other station in the antenna system beyond the pick-
up point for the feedback rectifier. Care must be used in designing such traps that they
do not cause sufficient phase shift to alter the phase-shift attenuation characteristic of the
transmitter seriously or instability may result.
The negative feedback will correct for distortion and noise, but only so long as there is
reserve capability in the system to effect the correction. For example, it cannot correct
for the distortion arising from overmodulation and, in fact, by introducing high-order
harmonics back into the circuit may actually increase the distortion if the system capabil-
ities are exceeded.
Since it is possible to keep the distortion of high-level modulated amplifiers down to a
fraction of a per cent by the methods discussed under Modulators, p. 7-74, negative
feedback is usually applied over the audio system, only, in this type of transmitter. This
eliminates the need for the r-f rectifier and largely eliminates the effect of the output
amplifier tank and load circuits on the performance of the feedback loop. The feedback
voltage is usually obtained from a voltage divider, connected between the plate of each
modulator tube and ground. The divider consists of capacitors, shunted by resistors.
These elements are proportioned so that their impedances are equal at a frequency of
approximately 100 cycles per second. The advantage of this type of divider over simple
resistances is mainly that the operation of the circuit is unaffected by the capacitance of
the leads connecting the network to the low-level audio-amplifier stage. Some improve-
ment in the phase characteristic is also secured.
The use of feedback permits high-efficiency linear amplifiers to be used in services such
as broadcasting, where low distortion and low noise level are essential. In high-level
transmitters, feedback, applied over the audio system, including the modulator, effects a
large reduction in noise and distortion and reduces performance variations due to non-
uniformity of parts and tubes. It also improves the modulator efficiency, permitting the
no-signal plate current to be reduced substantially to zero.
7-134 VACUUM-TUBE CIRCUIT ELEMENTS
31. AUDIO AMPLIFIERS
Broadcast transmitters are, by industry agreement, provided with enough audio gain to
produce 100 per cent sine-wave modulation with an audio input level of +10 db (1 milli-
watt reference level) at an impedance of 600/150 ohms. Special-purpose transmitters
may include more gain, although it is usually advisable to limit the gain so an input signal
of at least - 20 db is required. If enough gain is to be included in a transmitter to accept
a lower signal level, special shielding and filtering precautions are advisable to prevent
objectionable feedback.
Limiting amplifiers are generally used. A limiting stage may be designed into the audio
system of the transmitter, or an external line amplifier of the limiting-compressing type
may be used. Even in the latter case it is advisable to design one of the transmitter audio
stages so that positive modulation greater than 125 per cent is impossible, regardless of
the input signal level. Owing to switching transients or accidents, input levels 10 to 20 db
above 100 per cent modulation are bound to occur, and, unless they are prevented from
reaching the high-power amplifier by an absolute safeguard (such as driving the plate
current of an audio stage to cutoff), serious damage may result.
Many special features are incorporated in audio systems to meet the requirements of
particular services. Some of these are: automatic gain control, for circuits subject to
wide variations in level; pre-emphasis of high audio frequencies, used on conjunction with
complementary de-emphasis in the receiver to reduce noise; and scramblers which invert
or otherwise distort speech, making it unintelligible unless a receiver provided with a com-
plementary restorer is used.
32. TELEGRAPH TRANSMITTERS
For point-to-point transmission, telegraph code signals are often employed, since it is
generally possible to secure 100 per cent transmission with a much weaker signal when
telegraph is used instead of voice. Transmission may be accomplished either by tone
modulation, which directly replaces the voice transmission, by keying the carrier wave
directly (usually by overbiasing one of the intermediate amplifiers), or by shifting the
frequency of the carrier. The last method may be accomplished by shifting the carrier
a few hundred cycles back and forth at an audio rate and keying the audio signal or by
shifting the carrier between two fixed frequencies, several hundred cycles apart, one cor-
responding to the "mark" and the other the * 'space.'* Both these systems are akin to
frequency modulation and provide some advantage in noise suppression and diversity
effect without the complication of diversity receivers.
33, INSTALLATION OF RADIO TRANSMITTERS
TRANSMITTER TESTING. A great deal of test equipment is now available, making
it possible to examine conveniently all phases of the performance of a transmitter. Tests
generally performed are as follows:
1. Circuit check— by means of click meter, ohmmeter, etc., to be sure that wiring has
been done in conformance with wiring diagrams.
2. Control circuit check. Without tubes in any circuits, check the functioning of line
switches, starters, time delay relays, overload relays, interlocks, and circuit breakers.
No-load voltages of filament transformers may be checked at this time.
3. Transformer voltages. With filament circuits energized and tubes in place, check
filament voltages, transformer tap settings, range of primary voltage control, functioning
of air blower and/or water-cooling system.
4. Operational check. With all circuits tuned and functioning normally, check voltages
and currents on all elements of all tubes. Check for instability and parasitic oscillation.
5. Modulation characteristics. Under normal operating conditions, check audio har-
monic distortion at various modulation levels and at modulating frequencies throughout
the normal frequency-transmission range. The same test equipment is required for
s*e*K»rement of the frequency characteristic, and residual noise level, so these tests should
be performed at the same time. Figure 4 shows the equipment set-up required for this
test.
& IWer output. This test should be performed using loads representing the high-
aad low-knut load impedances which the transmitter may be required to feed To obtain
»ee«rafce power checks, the load resistance should be accurately measured and the load
INSTALLATION OF RADIO TRANSMITTERS 7-135
current determined by means of an accurate r-f ammeter; or the calorimetric method of
power measurement may be used, in which the increase in heat content of water used to
cool the dummy load is measured. The temperature rise of the water in degrees centigrade
multiplied by the number of gallons flowing per minute multiplied by the constant 264
will be equal to the number of watts of power dissipated in the load.
7. Heat run. The transmitter should be run under conditions of normal operation for
a period long enough for all components to reach approximately constant temperature.
The procedure set up by the RMA committee on amplitude-modulated broadcast trans-
mitters is a good example of how such a test should be run:
"The transmitter shall be operated (at rated power output) . . . long enough for all
components to attain temperature stability; that is, until the hourly increment does not
exceed 5 per cent of the total change under the following conditions: . . . The carrier
Measure modulation
capability and carrier shift
r—
1 Measure distortion
frequency characteristic
residual hum.
FIG. 4. Modulation Characteristics Measurements
should be continuously modulated by a 1000-cycle sine wave. The audio input level to
the transmitter shall be approximately 10 db below that corresponding to 100 per cent
modulation for not more than 98 per cent of the duration of the run and not less than
10 db above that corresponding to 100 per cent modulation for the remainder of the time." *
Temperature rise measurements of motor or generator windings, transformer windings,
etc., should be made by the hot-cold resistance method, in which the resistance and tem-
perature of the winding are measured after the unit has been out of operation long enough
to reach a uniform, stable temperature. The resistance at the end of the heat run is then
measured, and the rise in temperature is computed by the formula:
_ 234fi2
TI = temperature at which cold resistance was measured.
Tz — ambient temperature at end of heat run.
RI = resistance at TI.
JKs = resistance at end of heat run.
T « rise of winding temperature above final ambient.
8. Harmonic radiation. If the transmitter is tested using a dummy load, it is possible
to make a rough, check on harmonic intensity by coupling a field-intensity meter to the
load through an attenuator, shielding the field-intensity meter so that all its pick-up is
derived from the load. However, since dummy loads rarely ever even approximate the
impedance characteristic of an actual radiating antenna system, such tests are of little
quantitative value, and more satisfactory results will be secured if these measurements
can be made on an actual field installation.
* See Radio Manufacturers Association, Engineering Department, Standards Proposal 172, Elec-
trical Performance Standards for Standard Broadcast Transmitters.
7-136 VACUUM-TUBE CIRCUIT ELEMENTS
9. Incidental phase modulation. Instruments which will measure the degree of phase
modulation at frequencies below 40 Me are seldom available. The development of com-
mercial equipment operating in the 88-108 Me band for the purpose of measuring the
percentage of modulation of f-m broadcast stations, however, makes a handy tool availa-
ble for this purpose. The signal to be measured is multiplied up to a frequency within
the range of the meter by low-power harmonic amplifiers, and, since the meter is cali-
brated in terms of a 75-kc swing, the actual swing may be measured, and^then converted
into degrees of phase modulation, and divided by the multiplication ratio to determine
the actual amount of phase modulation at the transmitter carrier frequency.
10. Telegraph transmitter tests. In addition to the above tests, measurements are
made on the character of the keyed pulses of telegraph transmitters. The shape of the
keying wave, build-up, transients, breaks, etc., may be observed or photographed on the
face of a cathode-ray tube which has one pair of plates connected to a sample of the r-f
output of the transmitter, and the other pair excited by a sweep voltage which is prefer-
ably adjusted to synchronize the picture of the keyed pulse on the screen. The mark-to-
space ratio may be calculated by measuring the d-c current output of a rectifier energized
from the r-f output of the transmitter. The percentage of mark-to-carrier is given by the
ratio of the d-c current during keying to the current with key closed continuously. If the
former is designated IM , and the latter Ic, the mark-to-space ratio is
LOW-POWER TRANSMITTERS. Modern transmitters having a power output of
1 kw or less are usually designed as completely self-contained units. It is, accordingly,
only necessary to provide power line, audio input, antenna or transmission line, and any
necessary external monitor connections. Such transmitters are usually designed to
operate from either a 115-volt or a 230-volt single-phase a-c source. Power and audio
circuits may be conveniently brought into the transmitter through either conduits or
trenches; trenches permit somewhat greater flexibility for future change or modification.
External wiring and switching should be installed in accordance with fire insurance under-
writers' specifications. Ground wires should be connected by as short a run as possible
to a low-resistance ground, either the antenna ground system if any portion of it is in-
stalled near the transmitter or a separate ground consisting of copper plates buried in
moist soil. Antenna leads or transmission lines should be insulated, not only for the
normal operating potentials but also sufficiently well to protect against induced voltages
caused by lightning hits. A protective gap connected between antenna and ground will
discharge heavy induced charges.
HIGH-POWER TRANSMITTERS. High-power transmitters are usually designed so
that the equipment is segregated in accordance with a functional grouping, so that the
low-power audio-frequency equipment, for example, is well isolated from the high-power
r-f amplifiers. Each of these elements has somewhat unique installation problems and
will be considered separately.
Audio Equipment. If the transmitter is located some distance from the originating
point of the transmitted intelligence and connected to that point by telephone line or
radio relay, it is necessary to provide line terminating equipment to match the telephone
line properly and to restore the signal, attenuated by the line, to its original amplitude.
The necessary pads, line equalizers, line amplifier, together with the percentage-modula-
tion meter and transmitter-frequency monitor, are usually mounted in a standard tele-
phone-type rack in the operating room where they may be conveniently observed by the
transmitter operator. It is not ordinarily necessary to provide additional external shield-
ing for this equipment; however, it is necessary that it be adequately grounded through a
low-impedance and, preferably, separate ground lead. The incoming audio-frequency
circuits and the power supply wiring to the amplifiers should be carefully isolated from
each other, preferably by running in separate conduits, or, if in a common trench, by run-
ning the audio circuits in conduit. Audio-frequency circuits should use twisted pair
enclosed in a tight external shield.
Low-power Intermediate-radio-frequency Amplifiers. This portion of the equipment
resembles a low-power transmitter and requires no special comment beyond the points
already touched upon under that heading.
High-power Amplifier and Modulator. The installation of these units requires careful
planning since they must be installed so that they may be conveniently serviced and so
that the required high voltages, cooling air and/or water, and r-f output connections may
be conveniently made. Because of the relative simplicity and ease of maintenance, the
tread in design of high-power amplifiers has been toward the use of air cooling to dissipate
tfee heat generated in the plate circuits of the r-f amplifiers. For these transmitters provi-
BIBLIOGRAPHY 7-137
sion must be made for an intake for several thousand cubic feet of air per minute, and
means must be provided to exhaust this air after it has absorbed the heat developed in
the power amplifier tubes. Filters should be provided either in the transmitter or in the
air inlet. The exhaust air is frequently piped through ducts out of the transmitter into a
mixing chamber where it may either be diverted into the hot air heating system for the
building or exhausted outside. Because of the large volume of air required, the inlet duct
is frequently installed in the floor below the transmitter. It is possible to use this duct
also to carry interconnecting wiring out, but, because of the danger of a rapidly spreading
fire in case of an accidental short circuit in this wiring, this practice is not advisable.
Interconnecting wiring between the transmitter units should preferably be carried in
separate raceways which may be located in the building floor or arranged as troughs on
the side of the transmitter cubicles. All such raceways should be arranged so that they
may be conveniently opened for cleaning purposes and to permit changes in wiring as
required.
The r-f amplifier should be provided with a low-impedance ground connection pref-
erably in the form of a wide copper strap connected directly to a ground consisting either
of buried metal plates or a connection to the antenna ground system, if it is contiguous
to the transmitter building.
Rectifier and Power Equipment. It is desirable that the rectifier tubes be located so
that they may be observed by the operator at his normal position during the operation of
the equipment. Rectifier transformers, however, should be located either in a separate
vault or in a transformer yard, enclosed by a grill or fence outside the transmitter house.
Fire insurance underwriters' rules should be consulted and closely followed since these
rules differ from state to state and usually cover the installation of this type of equipment
in some detail.
SUBSTATION. The power line terminal equipment will ordinarily be supplied by
the power company having contracted to supply power. This equipment will include any
transformers necessary to change the voltage from the power company distribution voltage
to the voltage required at the transmitter terminals, together with necessary circuit dis-
connects, circuit breakers, lightning protectors, and metering equipment. To reduce the
possibility of outages resulting from a failure of the power supply, it is advisable, if pos-
sible, to provide for power feeds from two separate sources. Automatic equipment is
available which will switch from one line to the other in the event of a voltage failure.
To secure maximum advantage from such an emergency power supply, the transmitter
control circuit should be arranged so that a 1- or 2-sec voltage failure will not necessitate a
complete restarting cycle. Either manual or, preferably, automatic reapplication of
plate voltage should be provided after a no-voltage drop out, provided, for most rectifier
tubes, that such drop out does not exceed 2-sec duration.
BIBLIOGRAPHY
Coleman and Trouant, Recent Developments in Radio Transmitters, RCA Rev., Vol. 3, 316 (January
•i QOQA
Doherty, W. H., A New High Efficiency Power Amplifier for Modulated Waves, Proc. I.R.E., Vol. 24,
1163 (September 1936).
Lee, Reuben, Radio Telegraph Keying Transients, Proc. I.R.E., VoL 22, 213 (February 1934).
SECTION 8
FREQUENCY MODULATION
FREQUENCY-MODULATION SYSTEMS
ART< BY R. D. DUNCAN, JR.
1. Fundamental Relations
PAGE
02
FRE QUENCY-MODULATION
TRANSMITTERS
BY J. E. YOUNG
2. Frequency-modulation Broadcasting ---- 09
3. Frequency Modulation for Emergency
Transmitters ...................... 15
4. Transmitter Circuits ................. 15
FREQUENCY-MODULATION RECEIVERS
BY LESLIE F. CURTIS
5. Comparison with Amplitude-modulation
Receivers ......................... 16
ART. PAGE
6. Frequency Detectors 19
7. Limiters 24
DISTORTION AND INTERFERENCE IN
F-M SYSTEMS
BY B. D. LOUGHLIN
8. F-m Distortion from Non-uniform Am-
plitude and Phase Characteristics .... 26
9. Distortion Due to Incomplete Rejection
of Amplitude Modulation 27
10. Distortion Due to Multipath Reception 29
11. Cross-talk and Beatnote Interference.. . 29
12. Fluctuation Noise Interference 30
13. Impulse Noise Interference 31
8-01
FREQUENCY MODULATION
FREQUENCY-MODULATION SYSTEMS
By R. D. Duncan, Jr.
In frequency-modulation systems intelligence is communicated by variation of the
frequency or phase of the transmitted wave instead of its strength (as is done in ampli-
tude modulation ). Frequency modulation is used for broadcasting, for fixed-tp-mobile
stations, and for one- or two-way communication in services such as police, public-utility
maintenance, and forest patrol. It is being introduced into the truck, bus, taxicab, and
railroad fields. So-called "studio-transmitter link'7 equipment, which provides a one-
way radio connection in lieu of telephone lines between the broadcast studio and a remote
f-m transmitter, utilizes frequency modulation.
During the war, frequency modulation was much used in long-distance relay service,
and it is also used in domestic microwave relay service. It is employed in the allied fields
of facsimile and television broadcasting. In the latter, it provides the sound channel and
has been employed for relay operation. It has also been experimentally used for power-
line carrier current communication.
Frequency modulation is not well adapted to circuits subject to multipath transmis-
sion effects since serious distortion results from the simultaneous reception of several
signals differing slightly in phase.
1. FUNDAMENTAL RELATIONS
The modulating signal in frequency modulation causes the carrier frequency to be
systematically varied above and below the unmodulated value, the extent of the varia-
tion being determined by the strength of the signal. The number of times a second the
frequency is so varied is determined by the frequency of the signal.
This process of variation of the carrier frequency produces additional frequency com-
ponents, called sidebands, which lie both above and below the unmodulated carrier fre-
quency. Theoretically, there are an infinite number of such upper and lower sidebands
which differ in frequency from the carrier by the value of the modulating frequency or
frequencies and integral multiples thereof. However, then* amplitudes decrease rapidly
as they exceed in frequency value the upper and lower limits of the maximum frequency
swing imparted to the carrier so that satisfactory reception can be achieved by a trans-
mitting and receiving pass band somewhat greater than twice this maximum swing. An
important characteristic of frequency modulation is that the amplitude of the carrier
component as well as of the sideband components is determined by both the amplitude
of the modulating signal and by its frequency, or, in the case of a complex wave form, by
its component frequencies.
Another distinctive feature of frequency modulation is that, theoretically, the power
contained in the carrier and the infinite number of sideband components is a constant
value. That is, the transmitted power remains unchanged during the modulation if the
circuits are such as to transmit all the sideband frequencies. Practically, since only side-
bands within and just greater than the maximum frequency swing are transmitted, there
will be slight power variation during modulation, or a small amount of amplitude change
or modulation will accompany frequency modulation.
SINGLE-FREQUENCY MODULATION. A consideration of single-frequency modula-
tion will serve to illustrate the essential fundamental characteristics of frequency modula-
tion and the difference between it and phase modulation (see article 8-2 for methods of
generating frequency and phase modulation).
. the modulating signal is a single-frequency component, the expression for a f-m
be written in the form
E cos (<urf -f — sin pf) (1)
8-02
FUNDAMENTAL RELATIONS 8-03
where E = the maximum amplitude.
a? — 2 ir times the unmodulated carrier frequency.
p — 2 TT times the modulating frequency.
Aco = 2 TT times the peak frequency swing of the carrier.
The corresponding expression for a p-m voltage is
ep-m — E cos (cat + A0 sin pt) (2)
where A0 is the maximum phase or angle variation.
The difference between the two expressions is the (sin pt) term. For frequency modula-
tion the maximum phase or angle excursion is directly proportional to the peak frequency
swing, i.e., to the strength of the modulating signal, and inversely proportional to the
value of the modulating frequency, whereas for phase modulation, it is proportional only
to the strength of the modulating signal and is independent of its frequency.
A physical conception of the difference between frequency and phase modulation may
be had from Fig. 1. This shows a voltage vector E which without modulation during an
interval of time t has rotated counterclockwise through an angle
(o>i) . If it is assumed that an observer boards the vector, as it
were, so as to rotate with it, and modulation is applied, all that
will be noticed is a rocking back and forth of the vector through
the angle (d=A0), or a rotation first in one direction and then
in the other through the angle ( =b A0) , which may greatly ex-
ceed 360 deg. If the modulation is purely frequency type, it
will be noted that, with a fixed signal strength, the maximum
angular excursion will be greater for the low modulating fre-
quencies than for the high ones. If modulation is of the phase
type, no difference in the maximum excursion of the vector
will be noted for any modulating frequency. If the modu- FlG l Voltage Vector with
lating frequency remains fixed, there is no way of determin- * Phase Modulation
ing whether modulation is frequency type or phase type.
If amplitude modulation is also present, a slow periodic shortening and lengthening of
the vector would be noticed.
In the discussion on the mathematical equivalent of discriminator action (p. 8-09) it is
shown that the mathematical equivalent of f-m detection is to take the first differential,
with respect to time, of the variable angle through which the vector is rotating. For eqs.
(1) and (2) this angle is the argument of the cosine function. Doing this, the two follow-
ing expressions result.
For frequency modulation
— (cot -i sin pt) — o> 4* AOJ cos pt (3)
at
For phase modulation
— (co£ -f A0 sin pt} = co + p&6 cos pt (4)
The recovered signal is proportional to the periodic term in (3) and (4). For f-m recep-
tion, the maximum value of the signal is proportional to the extent of frequency swing
and is independent of the value of the modulating frequency. For f-m reception of a
phase-modulated wave, the maximum value of the signal increases directly with increas-
ing modulating frequency. By incorporating frequency-distorting circuits at the trans-
mitter or at the receiver, phase modulation may be converted into frequency modulation,
or vice versa.
The ratio AOJ/J? of Eq. (1) for frequency modulation was originally termed the "devia-
tion ratio" but is now referred to as the "modulation index," the last terminology also
applying to the angle A0 in eq. (2) .
The modulation index Aco/p plays an important part in the theory of noise suppression
in f-m systems and involves the circuit characteristics of both the transmitter and re-
ceiver. The FCC has established ±75,000 cycles (Aw = 2?r X 75,000) as 100 per cent
modulation for an f-m broadcast transmitter, with a channel band width of 200,000
cycles. It requires that the transmitter be capable of sustaining this maximum peak
frequency swing for any aural modulating frequency between 50 and 15,000 cycles, with-
out exceeding certain specified levels of harmonic distortion.
For this maximum peak frequency swing, the modulation index Aco/p would have a
value of 5 for a modulating frequency of 15,000 cycles and a value of 1500 for 50 cycles.
There would be five upper and lower sidebands within the overall swing band for the
higher modulating frequency and a maximum of 1500 sidebands for the lower frequency.
8-04
FREQTJENCY MODULATION
The standard for 100 per cent modulation for the sound channel of television broad-
casting is ±25,000 cycles with the same aural frequency band as f-m broadcasting. It is
suggested in the Standards, however, that the f-m transmitter be designed for satisfactory
operation at a peak swing of ±40,000 cycles. In the case of point-to-point communica-
tion services, such as police, the maximum overall swing band specified by the FCC is
three-quarters of the channel band. For the 30-50 megacycle band, one of the several
allocated for these services, the channel width is 40,000 cycles, for which the overall swing
band would be 30,000 cycles; 100 per cent modulation would then be ±15,000 cycles.
Assuming 3000 cycles as the maximum modulating frequency, the modulation index would
Substituting (P) for the ratio Aw/p in eq. (1) and for A0 in eq. (2), the equivalent side-
band form of expression may be written as follows:
e » E[JG(P) cos v* - Ji(P) cos (w - fit + Ji(P) cos (w + p)t
-f J2(P) cos (w - 2p)£ + ^s(P) cos (« -f 2p)t
- J3(P) cos (w - 3p)£ + Js(P) cos (w -h 3p)i (5)
+ J4(P) cos (w - 4p)« 4- /4(P) cos (w -r- 4p)t
- J6(P) cos (« - 5p) * 4- «/*(P) cos (co + 5p)t
+ J»(P){- l)n cos (« - np)t + Jn(P) cos (w 4- np)i]
The coefficients /.(P), Ji(P), J2(P) - - • J»(P) are Bessel functions of the first kind, of
order 1, 2 • • • n, and argument (P). Values of the argument (P) for frequency modula-
tion, as is shown later on, may vary from approximately 1 radian to the order of 1500
radians. For phase modulation, the maximum value for broadcasting is 5 radians.
For high values of the argument (P) , the approximate value of a particular order Bessel
function may be computed from the expression (see also Section 1).
(6)
Values of Bessel functions here involved, of zero order, for integral values of the argu-
ment from 1 through 9, and for orders 1 through 44, corresponding to integral values of
the argument of 1 through 29, are to be found in the book, Tables of Functions by Jahnke
and Emde. Values corresponding to decimal values of the argument, increasing. by incre-
ments of 0.2 from 0.2 through 6.0, and in increments of 0.5 from 6.5 through 16.0 for
orders zero through 13, are given in British Association for the Advancement of Science,
Reports on the State of Science, 1915,
i*0ie— , — i — i — I 1 — i — : — 5 — i — i — i — i — i — i — i on The Calculation of Mathematical
Tables, pp. 28-33.
For large values of the argument, the
reader is referred to Tables of Bessel
Functions Jn(x} for Large Arguments
by M. S. Corrington and W. Miehle,
Journal of Mathematics and Physics
(M.I.T.), Vol. 24, 30 (February 1945).
Argument values are presented in vari-
ous incremental groupings, extending
from 29 through 300, corresponding to
orders zero through 10. Values of the
specific function Jn(1000) corresponding
to order values of 935 through 1035 in-
creasing by steps of 1 are given in Tables
of Bessel Functions J"«(1000) by M. S.
Corrington, Journal of Mathematics and
Physics (M.I.T.), Vol. 24, 144 (No-
vember, 1945).
The first ten orders of the Bessel
function coefficients of eq. (5) are plotted
in Fig. 2. These curves show that,
(P) or modulation indices, Aco/p or
both positive and negative values
of any sideband component and
-0.4
01234
Y
Z\
56 7 8 9 10 11 12 13 14 15 16
Modulation iadex (P)
(a)
Fia 2a» Modulation Index (P)
depending upon the value of the argument
M* the different order Bessel functions have
and therefore pass through sero. The amplitude ._ „ —^^^^ „,..,
also o€ the carrier may be zero, that is. may be entirely missing from the f-m or p-m wave!
As is sfeown later on, this characteristic as it relates to the carrier component provides a
basis for measuring the extent of frequency swing or the degree of frequency modulation.
FUNDAMENTAL KELATIONS
8-05
Further illustrative of the relative amplitudes of the carrier and sideband components
and the frequency spread, as indicated in eq. (5) , values of the first ten order Bessel func-
tions are given in Table 1 for six values of the argument from 0.3 to 5. It is observed that
for values of the modulation index of 0.5 and less the amplitudes of the sidebands beyond
the first do not exceed approximately 3 per cent of the carrier. For a modulation index
0.4
0.3
0.2
0.1
0
-0.1
-0.2
-0.3
-0.4(
J3(P
>
-s
^
(?)f
Sl*tf
/
/*
\r
~<
\ /
^
V*"
-Je
(P)
f
/
/
\
A
\
\
-^
f
/,
/ ,
s\
i
\
^
1
s ,
N"
/^
s
.,
•^
^
^
s
\
\
\
\
1
X
/
k
\
y
\
>
J
\/
/
X
\
^
\
AS
A
/
/
\
^
V
^
^
^
*^-
s
"**^
) 1 23 4 5 6 78 9 10 11 12 13 14 15 1
Modulation index (P)
FIG. 2&. Modulatioa Index (P)
0.4
0.3
0.2
-0.1
-0.2
-0.3
-0.4,
j'7(pK
£e
(Pj
/-J
5<p
\
\
/
/
^
X
JS
N
^
^
\
/
/
/,
/^
/
\
\
\
\
/
^
s
^
^
\
\
s
S ,
Y
\
\
\
A
/
^
y
v, /
\j
\
^v.
^>.
_»x
~*s
0 1 2 3 4 5 6 7 8 9 10 11 12 13 14 15 16
Modulation index (P)
(c)
FIG. 2c. Modulation Index (P)
of 1.5, the third order sideband is approximately 12 per cent, and the fourth order, 2 per
cent, of the carrier. For values of 3 and 5 for the modulation index, all sidebands beyond
the sixth and eighth respectively are less than 1 per cent of the carrier amplitude.
Table 1. Values of Bessel Functions
Order
Argument or Modulation Index (P)
71
(P) = 0.3
(P) - 0.5
(P) - 1.0
(P) - 1.5
(P) - 3.0
(P) = 5.0
0
-f 0.9770
+ 0.9380
+ 0.7650
+ 0.5050
-0.26010
-0.17760
1
4-0.1490
+0.2410
+ 0.4401
+ 0.5600
+ 0.33910
-0.32760
2
+ 0.0112
+ 0.0300
+ 0.1149
+ 0.2330
+ 0.48610
+0.04657
3
+ 0.0006
+ 0.0025
+ 0.0195
+ 0.0615
+0.30910
+0,36480
4
+ 0.0024
+ 0.0113
+ 0.13200
+0.39120
5
+ 0.04303
+0.26110
6
+ 0,01139
+0.13100
7
+ 0.00254
+0,05338
8
+ 0.01840
9
+0.00250
Equation (5) with Fig. 3 illustrates additional differences between frequency and phase
modulation. Figure 3 (a) shows a carrier and sideband components for a modulation
index equal to 5 radians, and for a modulating frequency of 15,000 cycles. All the com-
ponents in this and the accompanying figures are plotted as positive regardless of their
polarity. For a modulation index of 5 and a frequency of 15,000 cycles, the peak carrier
frequency swing is 75,000 cycles. Figures 3(&) and (c) are for this same peak frequency
swing; (6) is for an aural frequency of 10,000 cycles and a modulation index of 7.5, and
(c) an aural frequency of 5000 cycles and modulation index of 15. Figures 3(<2) and (e)
8-06
FREQUENCY MODULATION
are for a fixed value of the modulation index of 5; (d) is for an aural frequency of 10,000
cycles and a peak frequency swing of 50,000 cycles, and (e) for a 5000-cycle aural frequency
and a 25,000-cycle peak frequency swing. Figure 3(a) is representative of both frequency
and phase modulation. Figures 3(6) and (c) are representative of frequency modulation
and Fig. 3(<Z) and (e) of phase modulation. .
For frequency modulation a decrease in the modulating frequency with a nxed peak
frequency swing increases the peak angle swing, alters the respective values of the carrier
and sideband components, increases the number of important sidebands within the fre-
quency swing band, and bunches the sidebands lying just outside of the swing band closer
•2TT x 15,000
0.4^W =
*> « X /3jUwu; \r j — ii, >/—*.<« * *«.
0.3
s
0.2
0.1
0
'
{
0
j f
O.3
0.2
0.1
0
V
*
FIG. 3. Sideband Distribution for FM and PM
to the peak swing limits. For the three aural frequencies considered, the first three side-
bands lying just beyond the swing limits, the outer one of which is less than 5 per cent
in value of the unmodulated carrier, occupy frequency spaces of respectively 45,000,
25,000 and 15,000 cycles.
Going to an extremely low modulating frequency, for example, 75 cycles, there would
be a maximum of 1000 upper and lower sidebands within the swing band with some
appreciable out-of-band components bunched relatively close to the swing limits. Math-
ematical analysis of this particular case has shown, that the fifteenth out-of-band com-
ponent which would be displaced by 1125 cycles beyond the swing limits is approximately
1 per cent in amplitude of that of the unmodulated carrier, with the further outlying side-
bands rapidly approaching zero.
It is to be concluded for frequency modulation that (a) for a given energy content the
higher modulating frequencies require a somewhat greater band-pass range from a circuit
design standpoint and (&) with decreasing modulating frequency the required band-pass
range approaches the overall frequency swing band in width. This last explains why only
the actual swing band need be considered when the frequency is varied at a very slow
ntfce, for example, by manual change of the capacitance of an oscillator, even though varia-
tiGa is over a relatively large range. It also explains why steady-state analysis, under the
assroopiion of a sinusoidal frequency variation at a low rate, may be employed in the
study of f-m circuits yielding results which, when properly interpreted, are sufficiently
aeeairate for design purposes (see article 2-8).
F wfcheraioire the fact that in the usual speech or music programs the energy of these
feigMreawnc^ tones is quite low keeps the modulation low and hence the magnitude of
feaoaoaiies <$ higher order.
FUNDAMENTAL EELATIONS 8-07
The practical result of these factors is that f-m systems work very well with the pass
band only slightly greater than the swing band.
In the case of phase modulation, decreasing the modulating frequency, with a fixed
phase swing, decreases the overall frequency swing, that is, bunches all sidebands closer
together, but alters neither the number of sidebands, their respective amplitudes, nor the
amplitude of the carrier.
If eq. (5) represents an f-m voltage wave, the rrns value is given by
2J?-(P) 4- 2J22(P) + 2JVKP) 4- 2/42(P) 4- 2/52(P) +•••]** (7)
The theory of Bessel functions shows that the quantity in the brackets approaches unity
as the number of terms becomes large. That is, the rms voltage of an f-m wave or the
power transmitted remains substantially at a constant value regardless of the extent of
modulation if a sufficient number of sidebands are present.
TWO-FREQUENCY MODULATION. Corresponding to eq. (1), the expression for
two-frequency modulation may be written in the form
et-m = E cos (cat -i sin pt -{ sin qt) (8)
P Q.
where IS, to, p, and Aco have the same meanings as before and q = 2w times the second
modulating frequency. The equivalent sideband form of this expression is given by eq.
(9), in which, as before, (P) = Aco/p is the modulation index of the p/2ir frequency, and
(Q) , substituted for Aw/tj, is the modulation index of the g/2-Tr frequency. For simplifica-
tion, this expansion is limited to the third-order Bessel functions of the two arguments.
The result of two-frequency modulation is the production of major sidebands involving
each of the two frequencies and, in addition, other sidebands involving the sums and dif-
ferences of the two frequencies and integral multiples of the same in different combina-
tions. The amplitudes of all sidebands are products of pairs of Bessel functions. Since,
for finite values of the argument, the values of all Bessel functions are less than unity, the
product of any pair will be less than the individual value of either of the pair. The change
from single- to two-frequency modulation thus greatly increases the number of sideband
components and the frequency spread or space occupied. However, the amplitudes of
all sidebands have been decreased in value so that, while the frequency spread has in-
creased, the outer sidebands have very low amplitudes.
A similar situation holds when more modulating components are added. That is, in
going from a single sinusoidal modulating signal to one of complex wave form the number
of sideband components is greatly increased, but their amplitudes automatically become
readjusted, or the total modulation is in effect divided between the components, so that
the overall frequency spread for all practical purposes undergoes little or no change.
e = J5yo(P)/o(Q) cos co£ - Ji(P)Jr0(Q}{cos (co - p)t + cos (co + P)t]
+ /2(P)/o(£) {cos (co - 2p)« 4- cos (co -f 2p)t}
- J3(P)/o(Q){cos (co - 3p)t + cos (co 4- 3p)«}
- /o(P)/i(£){cos (co - q)t 4- cos (co 4- q)t}
4- JWVaCQMcos (co - 2g)t 4- cos (co -f-
- </o(P)«/3«?){cos (co - 3q)t + cos (co + 3q)t}
s [« - (p - q}]t + cos la + (P -
— cos [co - (p + tilt -f cos [co 4- (P -f- tf)#f
cos [co - (p - 2q)]t - cos fa -f <j> -
+ cos [co - (p + 2q)}t - cos [u 4- (p +
(P) /,(Q) {cos [co - (p - 3<z)lt + cos fc 4-
- cos [co - (p -f 32)1* - cos |o> -f- (? 4-
8-08 FBEQUENCY MODULATION
+ /2(P)/i(Q) (cos [to - (2p - q)]t - cos [co + (2p - q)]t
— cos [w — (2p + q)]t — cos [w -h (2p + q)]t]
4- Ja(P) ^(Q)! cos [w — (2p — 2g)]i -f- cos [w + (2P —
-|- cos [w - (2p + 2<?)]i + cos [a? -h (2p + 2g)]i}
-f J2(P)Jz(Q) {cos [w - (2p - 3g)]f + cos [a? + (2? —
- cos [a> - (2p + 3«)]« 4- cos [a> 4- (2p 4- 3g)]i}
- J3(P)/!(Q) {cos [tf - (3p - q)]t + cos [w 4- (3p - Q)]t
- cos [w - (3p 4- «)]* + cos [w 4- (3p + ff)]*}
- Ji(P)/»(Q) {cos [a - (3p - 2ff)]« - cos [w 4- (3p - 2q)]t
4- cos [w - (3p 4- 2<z)l« - cos [a 4- (3p 4- 2q)]t]
- Js(P)/s(Q){cos I« - (3p - 3g)]« 4- cos [w 4- (3p -
- cos [a - (3p 4- 3fl)]« - cos [w 4- (3p + 3g)]«|
4-—] (9)
To avoid overmodulation on the peaks, the average modulation with a complex wave
form must be reduced. The necessity for such a reduction is well known in broadcasting.
MEASUREMENT OF FREQUENCY SWING. In the development, testing, and prac-
tical operation of f-m equipment, it is necessary to be able to measure the extent of fre-
quency or phase swing or modulation. The fact that the zero-order Bessel function J"o(P)
passes through zero with increasing values of the modulation index as shown in Fig. 2 is
made the basis for one useful method of measuring the peak frequency or phase swing.
In Table 2 are given the first five values of the argument (P) or modulation index for
which the sero-order Bessel function Jo(P) becomes zero. Other values may be obtained
from the references previously given.
Table 2. First Five Values of Argument (P) for Which J0(P) = 0
2.4048
5.5201
8.6537
11.7915
14.9309
In the operation of this method, a receiver of the heterodyne type is tuned to the un-
modulated carrier so that a beat tone of several hundred cycles is obtained. Single-fre-
quency modulation is then applied to the transmitter, the frequency being of a much
higher order than that of the beat tone. The strength of the modulating signal is increased
until the amplitude of the beat tone drops to zero, which for the first null corresponds to
the first passage through zero of the zero-order Bessel function «/o(P). From Table 2, the
value of the modulation index for this null point is 2.4048. The value of the modulating
frequency (p/2x) being known, the peak frequency swing (Aw/2ir) is obtained from the
ratio Aoj/p = 2.404S. Further increase in strength of the modulating signal will develop
additional null points corresponding to which values of the modulation index are given in
Table 2.
Another method of indirectly measuring the frequency swing provides a visual observa-
tion on the screen of a cathode-ray oscilloscope, of the carrier and sideband components in
their respective amplitudes and positions within a frequency band somewhat greater than
twice the swing band. In this method, the f-m signal wave is heterodyned to an inter-
mediate frequency of 2 Me, amplified, passed through an a-m detector, and supplied to the
vertical deflection plates of a cathode-ray oscilloscope. The heterodyning oscillator is
itself frequency-modulated by means of a reactance tube, with a 25-cycle linear-sweep
signal to peak values of plus and minus 100,000 cycles. The linear-sweep voltage is also
impressed on the horizontal deflection plates of the cathode-ray oscilloscope.
In action, the f-m signal wave, which consists of its carrier and sideband components,
la m effect "scanned" frequency-wise from 100,000 cycles below to 100,000 cycles above
^be csarrier, at a rate of 25 times a second. When, during this scanning process, a side-
band component or the carrier is encountered, a voltage pulse is impressed on the verti-
cal <l®Seetion plates of the oscilloscope. As the linear-sweep voltage is also impressed on
FREQUENCY-MODULATION BROADCASTING 8-09
the horizontal plates, the particular component will appear in its proper location within
the overall swing band.
THE MATHEMATICAL EQUIVALENT OF DISCRIMINATOR ACTION. In theo-
retical investigations of f-m systems, as with other communication systems, the end
product usually sought is a determination of the form of the received signal in comparison
with that of the signal originating at the transmitter.
An alternating voltage or current is represented by a vector of length proportional to
the maximum or rms value, revolving at an angular velocity equal to 2-n- times the fre-
quency, or, in customary nomenclature, <w = 2irf. In a given time t, the vector will have
rotated through an angle of (wi = 2-rr ft) radians. From the elementary theory of the
mechanics of planer rotating bodies, it is known that the angular velocity of rotation of
any point in the body about the axis is equal to the first differential of the instantaneous
angle of rotation with respect to the time. In the present case, this would be d(ut)/dt = co
= 2ir/; that is, the frequency is equal to the first differential of the instantaneous angle
with respect to time.
In conventional a-c theory, a vector revolves at a constant velocity as the frequency
has a constant value. In frequency modulation, the angular velocity varies with time, in
accordance with the modulation, about a mean or unmodulated value. The frequency
obtained by differentiation is therefore the "instantaneous frequency," which is what is
sought. The expression for the instantaneous frequency may be a simple periodic func-
tion of the modulating frequency or it may be a complex function requiring algebraic and
trigonometric operation or a Fourier analysis to break it down into the fundamental and
harmonic components.
Expressions are given above for a single- and a double-frequency-modulated f-m volt-
age wave and single-frequency-modulated p-m voltage wave. These are as follows:
(Aw \
art -\ -- sin pt \
(Aco Aw . \
o)t -\ -- sin pt -\ -- sin qt ]
P 9 /
ep-m — E cos (coi + A0 sin pt)
The first differential with respect to the time of the arguments of the three cosine func-
tions are, respectively, (co + Aco cos pt) and (co + Aco cos pt + Aco cos qt) and (« -f
j>A0cosp£). With linear detection the demodulated output is directly proportional to
these expressions. With square-law detection, the demodulated output is proportional
to the squares of the expressions and would contain second-harmonic components in addi-
tion to the fixed and fundamental frequency components. With a balanced discriminator
and differentially connected detectors, both the fixed and second-harmonic components
cancel out, leaving the fundamental frequency components of double amplitudes. Linear
detection is employed almost exclusively in commercial practice.
It is important to note that this mathematical method of recovering an f-m signal
implicitly assumes (a) that there is no amplitude modulation and (6) a linear input-output
characteristic of the hypothetical discriminator. It gives only the relative amplitudes of
the frequency components but tells nothing of their absolute values. If amplitude modu-
lation is present, the maximum voltage amplitude E in the preceding expressions is -also
a function of the time and must be taken into due account. Under most practical condi-
tions, it may be assumed that the effects of amplitude modulation are removed, by some
means such as limiting, leaving only the variable angle to be investigated.
FREQUENCY-MODULATION TRANSMITTERS
By J. E. Young
Transmitters for two major types of services are discussed in this section. These are
frequency-modulation broadcasting, which includes the sound transmitters used for tele-
vision broadcasting, and emergency communication.
2. FREQUENCY-MODULATION BROADCASTING
Frequency-modulation broadcasting has been assigned the frequency range from 88 to
108 me. This band has been divided into 100 contiguous channels with carrier frequencies
starting at 88.1 me and ending at 107.9 me. Transmission in each channel is permitted
8-10 FREQUENCY MODULATION
with a maximum frequency swing of 75 kc, which is designated 100 per cent modulation.
To insure that f-m broadcasting will be a high-fidelity service, the FCC has set up the
following standards for the overall transmitting system from microphone terminals to
antenna:
1. Distortion: less than 3.5 per cent, 50 to 100 cycles, 2.5 per cent, 100 to 7500 cycles
at 25 per cent, 50 per cent, and 100 per cent modulation; and 3.0 per cent, 7500 to 15,000
cycles at 100 per cent modulation.
2. Noise level: at least 60 db below 100 per cent modulation in the band 50 to 15,000
cycles.
3. Amplitude noise: at least 50 db below 100- per cent amplitude modulation in the band
50 to 15,000 cycles.
4. Frequency characteristic: the transmitting system shall be capable of transmitting
a band of frequencies from 50 to 15,000 cycles. Pre-emphasis shall be employed in accord-
ance with the impedance-frequency characteristic of a series inductance-resistance net-
work having a time constant of 75 microseconds. The deviation of the system response
from the standard pre-emphasis curve shall be between two limits. The upper of these
limits shall be uniform (no deviation) from 50 to 15,000 cycles. The lower limit shall be
uniform from 100 to 7500 cycles, and 3 db below the upper limit; from 100 to 50 cycles,
the lower limit shall fall from the 3-db limit at a uniform rate of 1 db per octave (4 db at
50 cycles); from 7500 to 15,000 cycles the lower Emit shall fall from the 3-db limit at a
uniform rate of 2 db per octave (5 db at 15,000 cycles).
Included in the system for which performance is thus specified are the microphone pre-
amplifier, mixers, program amplifier, studio-to-transmitter link, which may be wire or
radio, transmitter line terminating amplifier, and transmitter. The Radio Manufac-
turers Associatiom, working through industry committees, has specified the performance
of the components of the system so that it would be possible to combine elements of dif-
ferent manufacture without exceeding the distortion or noise limits specified. For the
transmitter, the following standards have been agreed to in the industry:
1. Distortion: audio distortion, including all harmonies up to 30 kc, shall not exceed
1.5 per cent rms from 50 to 15,000 cycles, and shall not exceed 1 per cent rms between
100 and 7500 cycles. Measurements shall be made at 25 per cent, 50 per cent, and 100
per cent modulation, for audio frequencies of 50, 100, 400, 1000, and 5000 cycles, also at
100 per cent modulation for audio frequencies of 7500, 10,000, and 15,000 cycles.
2. Noise level: at least 65 db below 100 per cent modulation in the band 50 to 15,000
cycles.
3. Amplitude noise: at least 50 db below 100 per cent amplitude modulation in, the band
50 to 15,000 cycles.
4. Frequency characteristic: shall not deviate more than 1 db from a straight line, or,
if pre-emphasis is used, from a 75-microsecond curve from 50 to 15,000 cycles.
F-M TRANSMITTER — SCOPE. Like the a-m transmitter covered in pp. 7-128, 7-137,
the f-m transmitter is considered to consist of all audio equipment operating above stand-
ard telephone-practice level and all r-f equipment from the source of the r-f oscillation
to the transmission-line terminals. Unlike a-m transmitters, f-m practice is to modulate
at low power levels, multiplying the frequency and power, usually many times, before
reaching the transmitter output.
FREQUENCY CONTROL AND MODULATION. Frequency control and modulation
are tied together since modulation is accomplished by actually swinging the frequency
back and forth in accordance with the modulating signal. To accomplish this, and still
keep the center, or average, frequency within tolerance (±2000 cycles for f-m broadcast-
ing) is one of the chief problems of f-m transmitter design.
Methods of frequency modulation may be divided into two basic systems. In one of
these, phase modulation, modulation is effected at some point in the circuit following the
oscillator, which is crystal-controlled. Modulation is accomplished by changing the
phase of the crystal-controlled signal at a rate corresponding to the desired modulation.
It is characteristic of p-m systems that the frequency shift is proportional to the modulat-
ing frequency aa well ass to its amplitude. To convert to true frequency modulation it is
necessary to compensate the frequency characteristic of tbe modulator, therefore, so that
the amplitude of the modulating signal is inversely proportional to its frequency. One
system of phase modulation is shown in the block diagram in Fig. 1. A crystal oscillator
liaving a frequency of approximately 200 kc is used to drive a balanced modulator in
wfeich the modulating signal is the audio frequency to be transmitted, and whose a-f
cliaraeteristie has been corrected to convert from phase to frequency modulation as
described alxmi. Tfee output of the balanced modulator consists of two f-m currents
whose deviations are instantaneously in opposite directions. These two signals are multi-
plied ia frequency 81 times through two separate channels of multipliers. One of the re-
FREQUENCY-MODULATION BROADCASTING
8-11
sultant signals is heterodyned to another frequency about 2 me removed. The resultant
frequency and the output of the second multiplier channel are then recombined and their
difference recovered. It will be noted that the difference frequency is independent of the
frequency of the original oscillator and depends only on the frequency of the 2-mc het-
erodyne oscillator. Additional multiplication of 48 times is then necessary to reach the
final operating frequency.
The phase modulation, at the point of its introduction, is usually restricted to less than
30° in order not to exceed permissible transmitter distortion. In the method described
Multiplier
(Six)
16,200 kc
Mixer
+5
rttfl
FIG. 1.
48
0-=2 x 485=2 x 48 x 81/^—75 kc max,
/=transmitter output frequency.
Frequency Modulation by the Phase-modulation Method
above, since two outputs are obtained from the balanced modulator having phase modu-
lation in the opposing sense, a total phase shift of 60° is possible. The multiplication
necessary to convert this phase modulation to frequency modulation, having a frequency
swing of ±75 kc, was, in this particular example, 3888 times. The use of dual p-m chan-
nels not only permits doubling the frequency swing but also makes it possible to cancel
out the effect of the 200-kc crystal in determining the transmitter frequency stability. In
the arrangement shown, the carrier frequency stability is a function only of the stability
of the 2-mc oscillator. Some improvement in f-m noise level is also obtained at the same
time.
Other methods of phase modulation have been developed which are quasi-mechanical
in nature. One of these, for which a special vacuum tube has been developed known as
the "Phasitron" tube, is used in some commercial f-m transmitters. The block diagram
of the circuit is shown in Fig. 2. A crystal oscillator operating at approximately 230 kc
Audio
Crystal
oscillator
230 kc
Network
<Pl
4>2 I
1*to3*
<M \
FIG. 2. Frequency Modulation Using the "Phasitron" Tube
(the exact frequency depends on the assigned station frequency) is coupled to a network
which, by means of tuned circuits, produces three outputs, all of the same frequency and
separated in phase by 120°. These outputs are applied to alternate wires of the deflec-
tor grid of the Phasitron tube in such a manner as to produce a rotating field. A cathode
and two anodes, which are at a positive d-c potential with respect to the cathode, are
arranged so that electrons are drawn from the cathode and focused into the form of a
tapered thin-edged disk. This disk, with the cathode for its axis, lies between a neutral
plane and the deflector grid structure and extends out to anode 1. The three-phase poten-
tial applied to the deflector grid structure deflects the electron beam so that the outer
edge of the electron "disk," if it could be seen, would appear to have a sinusoidally ser-
8-12
FREQUENCY MODULATION
rated edge which rotates about the cathode as a center, at a speed determined by the
three-phase voltage applied to the grid. Anode 1, located cylindrically around the cathode,
outside the periphery of the deflector grids, has 24 evenly spaced Dholes arranged around
its circumference; 12 of these are above the plane of the electron disk and 12 below. The
rotating serrated edge of the electron disk impinges on this series of holes. As the serra-
tions move around the periphery of the electron disk, the electrons alternately pass through
the holes to anode 2 and as the serrations move on one-half cycle are completely blocked
from anode 2. Thus the current flowing to this anode varies sinusoidally at the crystal
frequency. It follows, therefore, that any variation in the angular velocity of rotation
of the electron disk will result in a phase variation of the output current from anode 2.
A coil is placed around the outside of the tube so that the magnetic field resulting from
the current Sowing in the coil is perpendicular to the plane of the electron disk. The
electrons traveling radially out of the cathode toward the anodes through this field have
a force exerted on them in a direction perpendicular to their path and perpendicular to
the direction of the magnetic field. Thus, an angular displacement is introduced in the
rotation of the electron disk causing phase variation in the output of anode 2 as described
above. Consequently, if an a-f signal current of the proper amplitude flows through this
coil the output of the tube will be phase-modulated in accordance with this audio fre-
quency. When there is no audio signal input, the serrations about the periphery of the
electron disk will rotate at a constant amplitude, and the output frequency of anode 2
will be the same as the frequency of the crystal.
Phase excursions as great as 720° are possible, in this system, but if low distortion is to
be achieved the phase shift must be considerably restricted.
DIRECT FREQUENCY MODULATION. Direct modulation of the transmitter
master oscillator may be accomplished by several different methods. They all func-
tion by changing the reactance of the frequency-controlling part of the oscillator circuit
_^ Fm
output
Modulator —Screen Oscillator
FIG. 3. Frequency Modulation by Reactance Tubes
in accordance with the modulating frequency. One of the commonest of such systems
is the use of a tube or tubes having their plates connected to the oscillator circuit and
their grids excited by an r-f voltage derived from the oscillator tank and shifted in phase
90° with respect to the oscillator tank voltage. Plate current drawn by these tubes will
then be 90° out of phase with the oscillator output and thus has the characteristic of a
positive or negative reactance. The amplitude of this plate current is then varied by
means of the audio signal, which is also impressed on the grid, and, consequently, the
oscillator frequency shifts in accordance with the a-f signal. The basic circuit is shown in
Fig. Z.
Another method of achieving frequency shift in the master oscillator is to connect the
grid circuit of the modulator in parallel with the oscillator tank. See Fig. 4. In this cir-
Modulator
FIG. 4. Freqtieacy Modulation by Input Capacitance Variation
curi^ frequency modulation results from the fact that the input capacitance of the modula-
tor tube is a function of its plate circuit impedance and its transconductance, so that
FREQUENCY-MODULATION BKOADCASTING
8-13
It follows that, if the transconductan.ee is varied by the audio input signal, frequency
modulation in accordance with the audio input is obtained.
All the systems of direct frequency modulation have the common characteristic that the
transmitter frequency control is effected with reference to a separate, highly stable oscilla-
tor. These control systems may be divided into two categories, those in which the restor-
ing force is proportional to the deviation, and those in which full restoring force is de-
veloped regardless of the amount of deviation. In general, the latter will provide the
most accurate frequency control since the transmitter output frequency will be an exact
multiple of the reference oscillator frequency if the system is functioning properly. The
control voltage developed by the
error signal in either system may
be used to correct the master
oscillator frequency, either by
changing the bias of the tube used
to effect modulation or through
an electromechanical device driv-
ing a correcting capacitor in the
tank circuit of the oscillator.
One of the earliest of the first
type of systems is shown in Fig. 5.
A portion of the output of the
f-m oscillator, which is modu-
Reactance
modulator
Modulated
oscillator
To
ters
^
^
Discrirr
M
Reference
crystal
oscillator
FIG. 5. The Crosby Method of Frequency Control
lated by reactance tubes, is fed into a mixer, together with the signal from the reference
crystal oscillator. The beat between these two signals is fed into a discriminator tuned
so that it is working on the center of its characteristic when the frequency of the modu-
lated oscillator is the exact subrnultiple of the transmitter frequency. As the modulated
oscillator drifts away from the correct frequency, the beat signal fed into the discriminator
changes frequency accordingly and a d-c voltage is developed by the discriminator. This
voltage is applied to the grids of the reactance tubes in the proper sense to correct the
frequency of the oscillator. This method of frequency correction may be thought of as akin
to negative feedback, since the degree of correction is a function of the gain through the
mixer and discriminator, and the sensitivity of the reactance tubes.
One of the several variations of the second type of system is shown in Fig. 6. The
master oscillator is frequency-modulated by a reactance tube or other electronic means.
A sample of its output is divided in frequency by a locked-in oscillator, or multivibrator,
to a frequency low enough so that the carrier frequency will not vanish for any percentage
of modulation of any audio frequency in the normal pass band. For example, in one trans-
mitter the modulated oscillator has a center frequency of 4 Me, requiring a 3-kc swing to
achieve a 75-kc frequency swing at the transmitter output frequency. The center fre-
quency is divided by 256 so that
the frequency swing reaches a
maximum of 12 cycles per second,
If an audio modulating frequency
of 30 cycles per second is used,
the phase shift is then 0.4 radian
or 24°. This modulation index
reduces the carrier to 0.96 times
its unmodulated value; conse-
quently, a carrier frequency com-
ponent is always present to effect
synchronization. The output of
the reference crystal oscillator is
also divided in frequency, in
order to use a crystal which
can be easily manufactured, and
these two outputs are fed into a
Reactance
modulator
Mod
osc
ulated
Ilator
> - To
•
10-cycIe
low-pass
filter
Reference
crystal
oscillator
Divider
'
Div
der
Balanced
phase
detector
FIG. 6. Phase Detector Method of Frequency Control
balanced phase detector. If the two inputs to the phase detector are exactly 90° out of
phase its output will be zero. Any shift in phase difference away from the 90° point will
produce an output voltage with a positive or negative sign depending on whether the
phase shift is greater or less than 90°. This voltage is then applied to the modulator tube
grid to correct the frequency of the master oscillator.
A system of frequency correction utilizing an electromechanical circuit is shown in block
diagram in Fig. 7. In this circuit the oscillator is modulated by reactance tubes in the
conventional manner. A sample of the output of the modulated oscillator is divided by
240 and then fed into the grids of a pair of balanced modulators. The output of the ref-
8-14
FREQUENCY MODULATION
erence crystal oscillator is divided by 5 and then split through two phase-shifting net-
works, arranged to provide a 90° phase difference between the two branches. One of
these branches is fed into the grid circuit of one of the balanced modulators and the
other to the grid circuit of the second balanced modulator. If the divided down signal
from the f-m oscillator is in phase with the divided signal from the reference oscillator
there will be no a-c output from the balanced modulators. However, if there is any fre-
quency difference, an a-c voltage will be developed in the plate circuits of each of the bal-
anced modulators and the two voltages thus obtained will differ in phase by 90°. These
FIG. 7. Electromechanical Frequency Control
two outputs are connected to the two windings of a two-phase motor, and the shaft of
this motor is arranged to drive a small capacitor connected in the tank circuit of the f-m
oscillator. The a-c outputs of the balanced modulators, resulting from a frequency devia-
tion in the modulated oscillator, produce a rotating field hi this motor which tends to ro-
tate thejvariable capacitor in the proper direction to correct for the frequency error. As
soon as the frequency of the modulated oscillator has been restored to the point where its
submultiple is in exact synchronism with the submultiple of the crystal oscillator, the a-c
output of the balanced modulators drops to zero and the tuning capacitor comes to rest.
Another frequency-control circuit operating on a different principle is shown in the
block diagram. Fig. 8. In this circuit the outputs of the master oscillator and the crystal
oscillator are combined in a pair of mixers, in one of which the input from the crystal
oscillator differs in phase^by 9G° from the input to the other. The output of one of the
1 Reactance I ^
modulalor f
Modulaied
oscillator
To
multipliers
f
I Intfift-
f rator
Mixer-
L
•f45°
phase
shift
amp
r+-> *-*!
Discnm- I { DiscrLm- 1
tnator | { inator t
I Refa
r.ence
stal
ator
Mixer-
amp
<
-45°
phase
shift
1 o^'i
j ~~~i
1 Pulse 1
1 generator I
FIG. 8. Pulse Counter Frequency Control
mixers is fed through & pulse generator and thence through a pair of discriminators. The
eferimiaators are biased diodes. The bias on these diodes is set just above the peak
ralue of tte output of the second mixer. The result is that, when the pulses add to the
sine-wave output of the second mixer, the bias is overcome and the pulse is passed through
tins diode. Wfeea the pulse subtracts from the sine wave the bias prevents the diode from
©ondaefcing and the pulse is not passed. This arrangement serves to separate the pulses
into two ciixmits; o»e circuit is energised by one pulse for each cycle of beat between the
master oscilatoir aod the crystal oscillator when the signal frequency is high, and the other
TRANSMITTER CIRCUITS
8-15
circuit is energized by one pulse for each cycle of beat when the signal frequency is low.
The outputs of the two discriminators
are fed to an integrator, which is
simply a large capacitance and thence
to the grid circuit of a cathode follower.
The output of this tube is connected
to the tube which effects frequency
modulation, and thereby controls the
frequency of the master oscillator.
This circuit will tend to hold the center
frequency so that the frequency swings
higher and lower than the correct fre-
quency by the same total number of
cycles. The correction is continuous,
and the speed at which a frequency
shift is reflected in a correcting voltage
is a function of the time constant of
the integrating capacity.
3. FREQUENCY MODULA-
TION FOR EMERGENCY
TRANSMITTERS
Phase modulators, corrected to ob-
tain frequency modulation, are used
almost exclusively for this class of
service. The necessary degree of phase
modulation can be achieved with rela-
tively few stages of multiplication of
the f-m signal. This results from the
combination of two requirements that
greatly restrict the necessary p-m
angle. The first of these is that a com-
paratively narrow frequency swing is
used, varying from ±12.5 kc in the 25
to 30 Me band to =t22.5 kc in the 152
to 162 Me band. The second is that
the lowest unattenuated modulating
frequency need be no lower than 500
cycles per second. Thus, if a phase
swing of 1 radian can be obtained in
the modulator, a multiplication of only
45 is necessary to achieve a frequency
swing of 22.5 kc. Since considerable
distortion is tolerable before any loss
of intelligibility results, phase modu-
lators having much more inherent dis-
tortion may be used for this class of
service than for f-m broadcasting.
Overall distortion as high as 10 to 15
per cent has been found to have no
effect on the intelligibility of the signal.
Since most transmitters of this type
are portable, the most important char-
acteristics are small size and weight,
and the minimum number of tubes.
4 TRANSMITTER CIRCUITS
Because of the many times the f-m
signal must be multiplied, in f-m
transmitters, to obtain the necessary
frequency swing, the low power Fio. 9. Coaxial Tank Circuit
8-16 FREQUENCY MODULATION
stages operate through the frequency range covered by the section on a-m transmitters.
Additional care is required in f-m transmitter design to avoid high-Q circuits, since _ the
band -widths required are greater than in other transmitters. For the same reason, it is
desirable to use circuits that have symmetrical phase-shift characteristics about the center
frequency.
Output amplifiers for transmitters of power above 250 watts usually^ employ tubes
having internal capacitances great enough to necessitate the use of transmissi on-line-type
tanks. To avoid stray fields which might affect the operation of the exciter stages, and to
simplify the problem "of keeping the transmitter enclosure and outer conductor of trans-
mission lines at ground potential, these circuits are preferably made in the form of con-
centric lines. One such typical circuit is shown in Fig. 9. In this illustration a triode is
used. To avoid interaction between plate and grid circuits, the grid is grounded for r-f
voltages, and excitation voltage is applied between ground and the filament of the tube.
A three-quarter wave tuned transmission line is used and is in turn coupled to the output
of the driver by a small, single-turn loop. The plate circuit is a coaxial line, in which the
anode of the tube forms a continuation of the inner conductor. The line is tuned by
moving a by-pass capacitor provided with fingers which make contact with the inner and
outer conductor, along the line. Output coupling is obtained by positioning a loop in the
space between the inner and outer conductors. Control of the tightness of the coupling
is effected by changing the angle of the loop. Maximum coupling is obtained when the
loop lies along a radius of the outer conductor.
BIBLIOGRAPHY
Carson, John R,, Notes on the Theory of Modulation, Proc. I.R.E., Vol. 10, 57 (February 1922).
Armstrong, Edwin H., A Method of Reducing Disturbances in Radio Signaling by a System of Fre-
quency Modulation, Proc. I.RJB., Vol. 24, 6S9 (May 1936).
Crosby, Murray G.t Band Width and Readability in Frequency Modulation, RCA Rev., Vol. 5, 363
(January 1941).
Jaffe, David Lawrence, A Theoretical and Experimental Investigation of Tuned Circuit Distortion in
Frequency Modulation Systems, Proc. I.R.E., Vol. 33, 318 (May 1945).
FREQUENCY-MODULATION RECEIVERS
By Leslie F, Curtis
5. COMPARISON WITH AMPLITUDE-MODULATION RECEIVERS
Conventional f-m receivers use the superheterodyne principle and differ from a-m super-
heterodynes mainly in the i-f amplifier and in the second detector.
The intermediate frequency is chosen to give adequate image reduction depending on
the service. An intermediate frequency of 10.7 Me is suitable, and is specified as an RMA
standard, in receivers for f-m broadcasting in the assigned band from 88 to 108 Me since
the image response then falls outside the bands having assigned services which are liable
to interfere. A higher intermediate frequency of the order of 21.7 Me is required for the
sound channels of television receivers to avoid interference. The higher frequency is
favored in receivers incorporating both f-m broadcast and television facilities since the
same components may then be used for both.
The i-f band width should be sufficient to pass the side frequencies at the maximum
system frequency deviation without excessive attenuation of the power in any of them to
preserve the fidelity of the modulation. A band width of at least 150 kc for a reduction
of not over 50 per cent on the overall response curve at maximum deviation is required in
slightly rounded i-f response curve is preferred since double-peaked curves increase the
phase distortion within the receiver. The uniformity of response over the required band
should be as good as can be obtained with overcoupled or stagger-tuned i-f circuits if no
limiter is used. Receivers for special purposes which utilize narrow system deviations
commonly use limiters, and operate on the portion of the i-f response curve which is above
50 per cent of maximum.
It is possible to reduce the frequency deviation, and therefore the band width necessary
for tbe i4 stages, by feeding back some of the demodulated audio output to a reactance
tube associated with the superheterodyne oscillator to cause it to follow partially the
COMPARISON WITH A-M RECEIVERS 8-17
original frequency deviation. The distortion in the receiver and the overall noise-to-signal
ratio are reduced thereby, although the system is rather expensive.
The overall gain in an f-m receiver is usually greater than in an a-m receiver since satis-
factory reception may be had at very low levels of input to the antenna terminals, and
since, when a limiter is used, the input voltage at its grid terminals must be at least 1 volt.
In general, gain is uneconomical in the r-f stages at the frequencies assigned for f-m broad-
casting, and practically all the gain is usually obtained at intermediate frequencies. The
usual i-f plus converter gains are of the order of 10,000. The band width required lowers
the gain per stage, and usually one or two more i-f stages are required in an f-m receiver
than in an a-m receiver using the same types of tubes.
The frequency detector directly or indirectly converts the frequency modulation to
amplitude modulation and then recovers the audio signal by amplitude detection (see,
however, last paragraph of article 8-7) . Some means of reducing or preventing response
to spurious amplitude modulation due to noise and due to the variation in amplification
as the frequency is deviated over the i-f pass band is usually associated with the frequency
detector. This may be an amplitude limiter preceding the frequency detector, or the
frequency detector itself may be of a type which is non-responsive to amplitude modu-
lation.
A frequency detector with a balanced output, that is, one in which the net rectified
output is zero at the mean intermediate frequency, is preferred since spurious audio output
can then be produced only during deviation of the frequency due to the desired modula-
tion and is masked considerably by the latter. The d-c output of a balanced frequency
detector may be used to control the bias of a reactance tube associated with the oscillator
and thereby furnish automatic frequency control. De-emphasis circuits to compensate
for the pre-emphasis at the transmitter (corresponding to the voltage across an inductance
in series with a resistance when the combination- has a time constant of 75 microseconds) ,
and tone-control circuits, are usually included in the a-f system.
Antenna input systems, the superheterodyne oscillator, and the first detector are usually
the same in f-m receivers as in a-m receivers for about the same transmitted frequency
except that there is more tolerance in tuning and in frequency drift in f-m broadcast
receivers than in narrow-band receivers.
Automatic volume control may be incorporated and is desirable to keep the voltage
applied to the input of the limiter or non-amplitude-responsive detector at a level which
prevents overall response to rapid variations of the net antenna input voltage over as
wide a range as possible.
Certain types of f-m broadcast receivers are difficult for a novice to tune by hand since
there are multiple tuning positions where there is almost equal volume of response to the
desired program. Minimum harmonic distortion is obtained in only the position which
corresponds to the most linear portion of the frequency detector characteristic. The pro-
gram is demodulated in the other positions by the slope of the sides of the i-f response
curve and sometimes by the reverse slope of the skirts of the frequency detector charac-
teristic. A greater volume of even-harmonic distortion than fundamental often is pro-
duced between the several tuning positions for maximum response. Accurate tuning is
also required for the most effective reduction of response to impulse noise.
A zero-center-indicating meter operated by the d-c output of a balanced frequency de-
tector makes an excellent tuning indicator. It indicates zero for the proper tuning posi-
tion, and the direction of the deflection shows the direction of any mistuning. Twin
electron-ray tuning indicators, in which the illuminated portions of the opposite halves
are unequal except in the proper position, are sometimes used in broadcast receivers.
Receivers for operation in both the a-m and f-m broadcast bands generally use many of
the circuit components in both bands. The intermediate frequency for the f-m section is
much higher than for the a-m section, but transformers incorporating tuned circuits for
both frequencies are quite satisfactory. The r-f and converter stages tolerate a minimum
of switching because of the high frequency and are often separate for the two bands in the
more expensive receivers. The audio amplifier and power-output stages are usually com-
mon to both sectfons. Particular care in the design of the audio amplifier and sound
reproducer is justified since low harmonic distortion and excellent signal-to-noise ratio are
realizable with frequency modulation.
Figure 1 is the circuit diagram of the r-f, i-f, and detector portions of a low-priced fm-am
receiver. The desired band is selected by a ganged switch for the r-f, oscillator, converter,
avc, and detector circuits. Both bands are tuned with a two-gang condenser having sep-
arate stator sections for the two ranges. The f-m section includes a broad-band input
transformer for a 300-ohm transmission line, a tuned input circuit to the converter, and
delayed avc to obtain the proper input level for the ratio-type frequency detector. The
a-m section includes a condenser-tuned low-impedance loop and series loading coil, means.
8-18
FREQUENCY MODULATION
?
i *;
S l£>r-f<NO
H »{»
O'O'CD'O'
a<jsM
<cqcqco
ONW^-I
"5 o co *o TH oj t>T ^ S S 2 <N 55 S S
£ 1 ^^^.i^^Hr^Hr.^.H
§ I |||sal||as§sss
"o « 'o'o'o'o'o'o'o'o'o o"® *§,'§,'§
o »a>
oooooooooooowo
r-toOOOOOOOOO «,-<-<
ot>«ooooooo^N
r-'T^'ufc^'t-^o'o'cro
r-l CM •* O CNJ 1> O
THW^S
o
Si
O ^£
S 0°
o 3 ".«
s °. « S5
O N w ^C"
o- «0c? ° ?^
8 t|
00 °°
w-w^ r-,TO«^ ^2°.
OOOOOOOOOOOOOOOO
*^ O
O .
0 O OOO Q
i— ii— tCC*«w3O
I I i-tc
01 O
FREQUENCY DETECTORS
8-19
for additional antenna input from the leads of the 300-ohm line in parallel, and an un-
tuned input stage for the converter.
Crosstalk between common-channel f-m stations is reduced in receivers incorporating
good a-m rejection means to a point where only the modulation of the stronger of two
stations is audible. Cross-modulation in the stages of an f-m receiver due to the non-
linearity of tube characteristics is relatively small, whereas in a-m receivers it is one of the
major causes of interference at certain input levels.
Phase modulation differs from frequency modulation -only in the manner in which the
frequency modulation index (deviation ratio) is caused to vary with the modulating fre-
quency. In phase modulation it is proportional to the product of the amplitude and
frequency of a modulating component, whereas in frequency modulation it is propor-
tional to the amplitude of the component. Receivers for phase modulation are therefore
like receivers for frequency modulation, designed with an i-f band width suitable for the
maximum frequency deviation from the center frequency, but with an audio filter follow-
ing the frequency detector to restore the original amplitude of the modulating com-
ponent for the output. Pre-emphasis of the higher audio frequencies, as specified by the
FCC for f-m broadcasting, gives some of the characteristics of phase modulation to this
portion of the transmission.
6. FREQUENCY DETECTORS
Frequency detectors usually consist of some form of i-f slope filter which has a linear
variation in output voltage with frequency deviation to the maximum assigned deviation,
preferably fed with constant current from the last i-f amplifier, and followed by a con-
ventional amplitude detector. Detectors employing a phase shift between the voltages
applied to separate grids of multielectrode tubes corresponding to the frequency devia-
tion have been described but are not commonly used. Circuits which provide frequency
detection in a single tube and which are substantially unresponsive to amplitude modula-
tion are in the developmental stage. The detectors described herein have had commercial
application.
SIMPLE SLOPE FILTERS. A loosely coupled i-f transformer tuned to one side of the
mean intermediate frequency and operated at a point on the side of the resonance curve
where the response is about 72 per cent of maximum provides a simple slope filter. The
conditions differ with the coupling, but, for ex-
ample, when the coefficient of coupling between
primary and secondary windings is 0.3/Q, where
Q applies to both primary and secondary windings,
the variation in amplitude is substantially linear
over the range in frequency in which the amplitude
varies from 50 to 95 per cent of the maximum for
that stage alone. The frequency characteristic for
this condition is shown in Fig. 2. The Q of the cir-
cuits is reduced by loading so that Qf/F is 0.2,
where / is the expected frequency variation from
the mean and F is the mean intermediate fre-
quency. The frequency for maximum response for
the stage is separated from the mean frequency by
0.35 F/Q and may be either above or below it.
Full use of the most linear portion of the charac-
teristic results in 22.5 per cent amplitude modula-
tion, whereas a single tuned circuit provides only
15 per cent. The i-f amplifier is tuned to flatness
to operate about one of the operating points men-
tioned. Final demodulation is obtained in a con-
ventional diode rectifier following the filter.
1.0
0.9
0.8
0.7
0-6
0.5
0.4
0.3
0.2
0.1
0
c
%,
\
H-
0.2-
H
H
1
K
0.2
N
"1
\
1
\
N
1
^s
\
^
X
) 0.1 0.2 0.3 0.4 0.5
0.6 0.7 O.S 0.
FIG. 2. Frequency Characteristic of Slope
Filter
This type of frequency detector is not often used since it provides no inherent balance
against spurious amplitude modulation. The output due to impulse noise in this type of
frequency detector is much more disturbing than in one which is balanced for zero output
at the mean intermediate frequency.
DISCRIMINATORS. Discriminators as shown in Figs. 3(o) or 3(&) are used widely as
frequency detectors since they provide an inherent balance against amplitude modulation
at the mean intermediate frequency and require only a minimum number of components
and adjustments. The i-f voltages applied to the two diodes are respectively the sum and
difference of the primary voltage and one-half the secondary voltage of the transformer,
8-20
FKEQUENCY MODULATION
T-f Inpui
Whioh is tuned to the mean intermediate frequency. Since these vcJtag* Differ in phase
hv 00° at the mean frequency, the diode voltages are then equal. The rectified voltages
frequencies since the secondary voltage then lags by more than ^^rever^^tr^
quencies, and a directional
output substantially pro-
portional to the instantane-
ous frequency deviation
over a considerable range is
obtained. Thus an audio
voltage is available at the
output terminals which has
an amplitude proportional
to the frequency deviation
of the applied signal. A d-c
output which depends on
the difference between the
mean applied frequency and
the frequency to which the
unit is tuned is also devel-
oped if these are unequal.
Figure 4 illustrates typi-
cal shapes of characteristic
curves obtained in a dis-
criminator stage when the
primary and secondary in-
ductances and Q's are equal.
The curves are plotted in
terms of Qf/F, where f/F
is the ratio of the instan-
taneous frequency deviation
-i-B
FIG. 3. Discriminator Circuits
t/
to the center frequency. The actual output is obtained by multiplying the relative out-
put by VieQ-LcoI, where e is the rectification efficiency of the diode, L is the inductance
of the windings, w is the mean intermediate angular frequency, and I is the rms value of
the current supplied by the last i-f stage. The linearity and the magnitude of the output
are near optimum for the conditions shown when the product of the Q and the net coeffi-
cient of coupling between windings is about 2.7 although many similar curves may be
obtained when the primary and secondary
inductances and Q's are unequal.
It is important in obtaining a symmetri-
cal characteristic curve that the secondary
winding and circuit be symmetrical with re-
spect to ground. This requires that the center
tap on the secondary be placed properly, that
the coupling between the halves of the sec-
ondary be close, and that the leads to the
diodes be short and have no spurious couplings
to other parts of the circuit. The diode ca-
pacitances should be equal since that of one
aids, while that of the other opposes, the mag-
netic coupling between the windings. The
required Q, which includes the effects of
diode loading, and which may be reduced by
circuit loading if necessary to obtain the
proper band width, may be estimated from the
abscissas of Fig. 4 over which the linearity
is satisfactory for the expected ratio of f/F.
The coupling and by-pass condensers C are made only large enough to have low impedance
at- the intermediate frequency while their impedance at audio frequencies is large. The
caaarreat through each diode load resistance r should be only that rectified by the individual
diode. Any shtmt resistance across the output terminals, such as ra, is made large so
that the cwrent through it and the two resistors r in series will not bias appreciably the
diode delivering the smaller instantaneous output.
0.5
0.4
0.3
a 0.1
-0.2
-0.4
1.0
-(-1,0
+ 2.0
FIG. 4. Discriminator Characteristics
FREQUENCY DETECTORS
8-21
The i-f choke shown in Fig. 3 (a), which is effectively in parallel with the primary in-
ductance, may be omitted if the diode loads are connected as in Fig. 3(&). This is permis-
sible if the desired Q can be obtained with the increased loading effect which the diodes
present for this connection. Each individual diode presents a load of r/1.8 in Fig. 3 (a)
and r/2.8 in Fig. 3(6), where r is as indicated in the figures, and the diode rectification
efficiency has the usual value of about 90 per cent. The desired Q may be obtained
either by loading the windings, as with r& or by designing the individual windings with
the diameter and spacing of turns which result in the required value.
The frequency at which the response is zero is adjusted by tuning the secondary circuit
of the discriminator. The symmetry of the response curve about the zero point is ad-
justed by tuning the primary circuit. This procedure is easier than adjusting each indi-
vidual circuit for resonance at the center frequency.
Some special-purpose receivers are arranged to respond to either frequency modulation
or amplitude modulation in the same transmission band by providing a reversing switch
for one of the diodes of the discriminator. "When one is reversed from the polarity indi-
cated in Fig. 3, the sum, rather than
the difference, of the rectified voltages
is applied to the output , which is proper
for the demodulation of a-m waves.
SIDE-TUNED CIRCUITS AS FRE-
QUENCY DETECTORS. Another
frequency detector which has zero out-
put at the mean intermediate fre-
quency consists of separate tuned cir-
cuits C%Lv and CzLz individually tuned
slightly above and below the center
4-B
FIG. 5. Frequency Detector with Side-tuned Circuits
1.2
,.1
frequency and connected as shown in
Fig. 5. The response curve is shown in
Fig. 6. The stage is tuned by adjusting the peaks of the S curve, each of which depends
chiefly on the tuning of one of these circuits but is influenced slightly by the tuning of the
other. An alternative tuning method is to transfer the connection between the two tuned
circuits from the full-line to the dotted-line connection after tuning both circuits to the
center frequency. The incremental inductance L is chosen to shift the resonance by the
proper amount in opposite directions.
Neglecting the coupling between the two side circuits caused by the common primary
circuit CiZ/i, to which they are individually coupled, the best -linearity of the characteristic
is obtained when fi/F — 0.75/Q, where A is the
frequency displacement of either resonant side
circuit from the center frequency. The relative
output for this case is shown in Fig. 6 plotted
against relative instantaneous frequency devia-
tion Qf/F. The actual output depends on the
coupling to circuit CiZ/i. The capacitance C\
of the driving tube may be tuned out at the
center frequency, and the effects of the primary
circuit over the band may be minimized by
loading it with resistance. The presence of the
tuned primary circuit slightly improves the
linearity of the S curve near its peaks by an
amount not shown in Fig. 6, and depending
on its coupling with the side circuits. To ob-
tain the best linearity for both positive and
negative deviations it may be necessary to
use slightly different Q's in the two side cir-
cuits and slightly different coefficients of
0.6
-0.4
-0.8
-1.0
7_
j_
^.O-O.a-o.6-0.4-0.2 0 0.2 0.4 0-6 0.8 i.o coupling between the primary and these cir-
***' cuits. Such expedients compensate for the
Frequency Characteristic with Side- fact that the resonant peaks of the side circuits
tuned. Circuits , , , , _.
are not at the same frequency.
RATIO-TYPE FREQUENCY DETECTORS. One type of frequency detector which
can be made to be non-responsive to any undesired amplitude modulation has been called
a ratio detector, since the net output is approximately proportional to the ratio of the i-f
voltages applied to the two diodes, although the process by which this is accomplished is
indirect, and a more complete analysis shows that the ratio of the circuit impedances
rather than the voltages is involved. Two of many possible arrangements are illustrated
8-22
FKEQTJENCY MODULATION
I-f input
A.V.C.
Ratio-type Frequency Detector Circuits
in Figs. 7(o) and 7(&). In Fig. 7 (a) the filter is quite similar to the discriminator previously
described except that the components are designed to tolerate a greater a-c load current.
In Fig. 7(6) the side-tuned
circuits CzL® and CzL$ are in
^ series with no magnetic cou-
p~1 J~^~ pling to the choke feed L1?
6H6/f~~K "T'lcgi7" while capacitance Cj is as
-e* — small as possible to reduce
the undesired coupling be-
tween these circuits. In both
arrangements condensers C
are only large enough to have
low impedance at the inter-
mediate frequency.
The diodes are in series and
are therefore forced to carry
the same rectified load current
which charges a large electro-
lytic condenser Ce to a voltage
which depends on the mean
i-f signal level. During de-
sired frequency modulation or
un-desired amplitude modula-
tion, this voltage, all or a part
of which may be used also for
automatic volume control, remains constant and establishes conditions for the mean rec-
tification efficiency of the diodes and for a voltage drop
in the a-c impedance of the source. The action is
illustrated by the diagrams of Fig. 8 which are not to
scale but show, diagrammatically, superimposed regu-
lation curves for the diodes (one inverted to show the
division of the electrolytic condenser voltage E} for
several conditions. Figure 8 (a) shows the relations
between the output current and the component volt-
ages which lead to operation at a particular value of
outptit current at one input level and frequency. The
peak voltages applied to the input terminals of the
diodes are J£\ and E$ respectively. They have maxi-
mum values for no rectified current since the a-c diode
input current is from 1.67 to 2.0 times the rectified
current, depending on the rectification efficiency of the
diodes. The rectified voltages* whose sum is Et are the
input voltages multiplied by the individual rectification
efficiencies and are ei and & respectively. The diodes
are in series, and the common-current operating point
is skown by the marked intersection.
The a-c diode input current is in phase with the in-
put voltage, but the filter networks carry substantial
reactive components of current. Furthermore, the re-
lations between the diode input and output currents and
voltages are non-linear. Therefore the characteristics
cautnot be expressed readily in terms of the circuit con-
stants. However, each circuit and associated diode has
a definite regulation curve for each frequency and for
each current level supplied by the last i-f tube. The
effective impedance whidb determines the output volt-
age drop in terms of the output current depends pri-
marily on the impedance of the tuned circuits and
secondarily on nonlinear functions of the current and Rectified output current
FIG. 8. Regulation Curves in Ratio-
type Frequency Detectors
Rectified output current
(a)
Rectified output current
(&)
8(&) stows the effect of deviating the fre-
Tfefe changes the filter impedances and con-
sequently the effective output impedance and the slope
«i tin* insulation curves. The difference between either diode output voltage and its mean
vafafe, M/Z, vsunes ai th« modulating frequency and represents the desired audio output.
FREQUENCY DETECTORS
8-23
Figure 8(c) shows the effect of amplitude modulation of the input signal at a given
frequency. The voltage E remains constant at its mean value by virtue of the charge on
the electrolytic condenser. The output current varies instantaneously with amplitude
modulation although its mean value is substantially constant. If the degree of inward
modulation is sufficient to reduce the rectified current to zero as illustrated by the dotted
lines, rectifying action is lost and intolerable distortion results. The resistance r is made
smaller than in conventional discriminators to allow for a margin in inward modulation
without reaching these limits. The ratio of the uniform signal to the instantaneous signal
which will produce cut-off is the overdrive and should be at least 2 to 1. It is particularly
important that the relations be so chosen that the detector is not cut off when the instan-
taneous voltage swings to its lowest value as the frequency is deviated over the selectivity
response curve of the receiver.
It can be shown that with ideal diodes with rectification efficiencies of 100 per cent, and
with non-reactive source impedances, the output voltage e is independent of amplitude
modulation when the short-circuit currents I8, as shown by the regulation curves, are the
same for the two diodes. The output is then e = Q.5E(Zi — Z£/(Zi + Z2), where Z\
and #2 are the impedances of the two filter sections. In actual ratio-type frequency de-
tectors the phase angle of the filter impedance
varies with the frequency deviation and the
diode efficiency depends on both applied
voltage and rectified current. It is therefore
difficult to compensate perfectly for ampli-
tude modulation over a wide range of either
signal level or deviation. The best combina-
tion of impedances is determined by trial
.For the circuit of Fig. 7(a), for example, opti-
mum values of coil inductance L% and L\,
mutual inductance m, resistance r, and capac-
itance C will be found for a particular type
of tube and range of operating levels for the
best linearity of desired output and reduction
of amplitude modulation.
Some of the possible detector characteris-
tics for simultaneous amplitude and frequency
modulation are illustrated in Fig. 9. The
curves drawn with heavy lines show the output
during maximum outward amplitude modu-
lation. Figure 9 (a) is for a conventional dis-
FIG. 9. Amplitude Compensation in Ratio-type
Frequency Detectors
criminator without the compensating effect of the ratio-type detector. Figures 9(6) and
9(c) are for partial and overcompensation respectively. In (c) high input level produces
less output over a portion of the deviation range than lower input.
The diodes carry components of current at the second-harmonic frequency as well as
at the fundamental frequency. This current returns through the filter sections and pro-
duces a small second-harmonic voltage which shifts the effective phase of the peak voltage
to be rectified. This effectively detunes the filter sections synchronously with the ampli-
tude modulation and accounts for an unbalanced characteristic as illustrated in Fig. 9(c£)
between two signal levels. When the variation in input level is due to deviating over a
non-uniform selectivity response curve of the receiver, the resulting characteristic may be
as shown by the dotted line.
The demodulated signal rises and falls with the applied signal when it is varied slowly,
as in tuning. This is an advantage, since the proper tuning position is then indicated by
maximum volume.
Since a large degree of reduction of amplitude modulation is obtained in the ratio-type
detector stage itself, limiting in the previous stages is not always required, and the signal
level at the last i-f tube need not be as high as in receivers using limiters. Automatic
volume control may provide sufficient control of signal level.
Multipath transmission through space of the signal applied to the antenna terminals of
the receiver may result in amplitude modulation sufficient to reduce the instantaneous
input to the diodes in a ratio-type detector below their cut-off level, and in this case a
receiver having high i-f gain followed by limiter is superior.
8-24
FREQUENCY MODULATION
r+B
FIG. 10. Grid-bias Limiter
7. LIMITERS
An ideal limiter or limiting system for operation at the intermediate frequency of an
f-m receiver delivers an rms output which is independent of the ^input when the input is
above a threshold level. (However, a proposed type "dynamic limiter gives output
proportional to the average input but wipes off any a-f amplitude modulation.) It should
operate instantaneously and therefore should not include time-constant circuits which
delav its recovery after being subjected to a high input voltage, as, f or ^example, a burst
of impulse noise. The loading effect of the limiter on associated tuned circuits should not
change with signal level. , -, i • i_ -xi_
The greatest value of a limiter is in reducing amplitude modulation, synchronous with
the desired frequency modulation, which may be introduced by the deviation of the fre-
quency over symmetrical but slightly rounded i-f response curves. It is also of value in
reducing random or impulse noise which occurs while the carrier is deviated from the
GRID-BIAS LIMITERS. Limiters in which the operation is controlled by the bias
developed by grid rectification are more commonly used than other types. The funda-
mental component of the plate cur-
rent of a grid-bias limiter is main-
tained substantially constant over a
considerable range of input (usually
about 10 to 1) by a proper correla-
tion of the bias developed at these
levels with the bias necessary to cut
off the instantaneous plate current, .
thereby compensating for the change
in angle in each cycle over which the
plate circuit is conducting. This re-
lation is most easily obtained in a
pentode tube since its plate current
is nearly independent of the plate load. A typical circuit is shown in Fig. 10. The out-
put is applied to a circuit tuned to the fundamental frequency (usually the discriminator) ,
and the harmonics are filtered out. A sharp-cutoff tube is used since limiting may then
be obtained at low input levels.
A typical grid-bias limiter static characteristic is shown by the solid line in Fig. 11. If
the grid resistor is too small, the efficiency of grid rectification and the developed bias are
too small, so that the angle of plate conduction is not reduced sufficiently at high input
levels, and the output current rises, as shown by the upper curve. Conversely, if the grid
resistor is too large, the output falls as shown by the lower curve. At very high input
levels the proper relations cannot be held for any proportions and the output again rises.
Although the static characteris-
tic of a grid-bias limiter may be
made flat over a wider range
than shown by placing resistors
by-passed to ground in the plate-
or screen-supply circuits, the
overall operation in the presence
of impulse noise is not satisfac-
tory since the conditions follow-
ing a burst of noise are not
normal and the output suffers
during the recovery time of the
plate or screen circuits.
An approximate rule for flat
limiting which holds for pentode
tubes may be used if the co-
efficient a in the expression % = ae$& for the grid current ig in terms of the instantaneous
applied grid voltage e is known. The product arJG?eH should be 35 or 40, where r is the
grid resistor in ohms and Ec is the d-c grid voltage necessary to cut off the plate current
with the screen voltage selected. The rms plate current is then approximately Q.5gmEc
in the range of rms input voltage from 0.7 to 7.01<?c, where gm is the transconductance of
the tube with small negative bias at the screen voltage selected. The level at which limit-
ing occurs with common tubes is ordinarily between 1 and 3 volts but may be adjusted
over a small range by selecting the screen voltage.
~o
-o
c
« o
if
^1
Y
,-<:
^
~~~ -— *
**^
_.. «-»•"'""
Relailve outout vol
s
-
"""""--—
—
/_
0 -10 0 -t-10 +20 +30 +4C
R&lative input voltage In decibels
FIG. 11. Grid-bias Limiter Characteristics
BIBLIOGRAPHY 8-25
Cascaded limiters are often used to cover a greater range of input signals over which
limiting is effective. The voltage applied to the grid of the last limiter from that developed
in the tuned output circuit of the previous limiter is made to fall at a point below the final
upward curvature of the static characteristic so that an additional 10-to-l range in level
may be handled. All the i-f tubes may act as limiters when the i-f amplifier is used only
for f-m signals. The rectified d-c voltage in the grid resistor may be filtered and used for
avc bias.
The time constant of the r-C combination in the input circuit of a grid-bias limiter should
be as short as is consistent with little loss of i-f gain. The recovery time is then fast enough
so that the program is not eliminated for an audible interval after a burst of impulse noise.
PLATE LIMITER. A plate limiter operates when the plate voltage of a triode or
pentode swings downward to that portion of the plate-current plate-voltage characteristic
where an increase in grid voltage in the positive direction produces no increase in plate
current. The stage is operated with very low plate-supply voltage and with a high-
impedance plate load. During negative grid voltage swings the plate current is cut off.
The instantaneous output current swings between the maximum and zero, and tends to
deliver a rectangular wave at high input levels. The rms output voltage increases slightly
with increase of input level until the output current has assumed the rectangular wave
form, and is then somewhat less than half the plate-supply voltage. The harmonics of
voltage in the output are eliminated in the tuned circuit.
Heavy grid current loads the input circuit of a plate limiter during positive grid swings.
This may be restricted by a resistor in series with the grid lead but may still influence the
selectivity and gain of the input tuned circuit. A plate limiter has the advantage of rapid
recovery time if the plate- and screen-supply voltages are not influenced by the tube load
but is more often used in clipping and shaping pulses than in amplitude limiting in f-m
receivers.
LOCKED-IN OSCILLATOR. An oscillator operating at the intermediate frequency
or some submultiple thereof may be used to cause the receiver to be non-responsive to
amplitude modulation and may be synchronized or locked in by the i-f signal and then
follow its deviation. An oscillator remains in synchronism over a wider band, and its
output is slightly greater, for high signal inputs than for low. It has been found to be
most satisfactory when operated at a submultiple of the intermediate frequency. It then
has the advantage of having an output frequency which will not feed back to the previous
i-f stages. However, it requires an input signal above 1 volt and in this respect is no more
satisfactory than a grid limiter. Discriminators for use with synchronized oscillators must
be specially proportioned to take care of the interaction with and the loading of the oscil-
lator circuits.
A frequency detector which operates as a locked oscillator in which the frequency is
controlled over the deviation range by quadrature feedback from the plate circuit of a
heptode tube, and which simultaneously provides an audio output in the plate circuit, has
been described. The output is linearly proportional to the frequency deviation and is
independent of i-f amplitude, provided the latter is great enough to maintain synchronism,
BIBLIOGRAPHY
Argnimbau, Discriminator Linearity, Electronics, Vol. 18, 142-146 (March 1945).
Armstrong, B. H., A Method of Reducing Disturbances in Radio Signaling by a System of Frequency
Modulation, Proc. I.R.E., Vol. 24, 689-740 (May 1936).
Beers, G. L.» A Frequency-dividing Locked-in Oscillator Frequency-modulation Receiver, Proc. I.R.E.,
Vol. 32, 730-737 (December 1944).
Bradley, W.?E., Single-stage F-m Detector, Electronics, 88-91 (October 1946).
Carnahan, C. S., and Kalmus, H., Synchronized Oscillators as F-m Receiver Limiters, Electronics,
Vol. 17, 108-111, 332-342 (August 1944).
Crosby, M. G., Frequency Modulation Noise Characteristics, Proc. LR.E., Vol. 25, 472-514 (April
1937).
Meyers, S. T., Non-linearity in Frequency-modulation Radio Systems Due to Multipath Propagation,
Proc. LR.E.t Vol. 34, 256-265 (May 1946).
Roder, H., Amplitude, Phase and Frequency Modulation, Proc. I.R.E., Vol. 19, 2145-2176 (December
1931).
Smith, D. B., and Bradley, W. E., The Theory of Impulse Noise in Ideal Frequency-modulation Re-
ceivers, Proc. LR.E., Vol. 34, 743-751 (October 1946).
Wheeler, H. A.t Common-channel Interference between Two Frequency-modulated Signals, Proc,
LR.E., Vol. 30, 34-50 (January 1942).
8-26
FREQUENCY MODULATION
DISTORTION AND INTERFERENCE IN F-M SYSTEMS
By B. D. Loughlin
In f-m systems, just as in a-m systems, distortion can result from a non-linearity of the
input-output characteristic of the modulator or frequency detector. However, the modu-
lator of the transmitter can generally be properly designed to have a substantially linear
input-output characteristic over the operating range. In the commonly used phase
modulators which are inherently non-linear for large phase deviations, satisfactory lin-
earity is obtained by restricting the operating range to use small phase deviations at the
modulator, followed by frequency multiplication to obtain the desired frequency modula-
tion. It is also relatively straightforward to obtain linear frequency detection from the
commonly used f-m detectors when they are receiving an ideal f-m signal of constant
amplitude. Thus the commonly used frequency modulators and detectors are generally
designed so that they contribute only a small amount of distortion to the f-m system.
This section treats the special lorms of distortion which are unique to an f-m system
and which arise from translating the f-m signal through the amplifiers of the transmitter
and receiver and through the transmission medium. When the f-m signal passes through
the amplifiers of the transmitter or receiver, f-m distortion can result because of inade-
quate band width, or non-linear phase characteristic. Also, if the transmission charac-
teristics of the amplifiers are not flat over the frequency deviation of the applied signal,
spurious amplitude modulation synchronous with the frequency modulation is introduced,
which may cause distortion if there is incomplete rejection of amplitude modulation by
the f-m detector system. Another serious form of f-m distortion, producing both spurious
amplitude and frequency modulation, results from multipath transmission between the
transmitter and receiver.
Netwoi*
characteristics
a F-M DISTORTION FROM NON-UNIFORM AMPLITUDE
AND PHASE CBARACTERISTICS
When an f-m signal is translated through an amplifier or network having a non-uniform
amplitude or phase characteristic, some spurious frequency modulation (in other words,
f-m distortion) results. The f-m distortion results
because the various sideband components of the f-m
signal are translated with different amplitude and
delay and thus do not correctly combine in the out-
put. The first approximation to the distortion can
be obtained by a quasi-steady-state analysis. In a
quasi-steady-state analysis, it is assumed that at any
instant the f-m signal is translated with an amplifi-
cation and delay determined by the steady-state
amplitude and delay characteristics measured at a
frequency equal to the applied instantaneous fre-
quency. The delay used is, of course, the envelope
delay, that is, the slope of the phase characteristic
at the particular frequency.
To illustrate the quasi-steady-state solution, as-
sumed amplitude and phase characteristics, with
the resulting delay characteristic, are shown in Fig.
1. An applied f-rn signal with a sine wave of modu-
lation is shown together with the resulting output
signal instantaneous frequency and amplitude
modulation. It can be seen that the non-uniform
amplitude characteristic introduces spurious am-
plitude modulation and no f-m distortion but that
the non-uniform delay results in an f^m distortion
FIG.
Quasi-steady-state Approxima-
tion for F-M Distortion
<J«e to different delay for different parts of the audio cycle. The resulting distortion can
be found by a graphical Fourier series analysis, or a Fourier series expansion of the output
f-m equation. In accordance with this approximate analysis method the output frequency
saodnlatkm would be:
f .m. = a sin p(t — t&) (1)
wfeere a = maximum frequency deviation, p = angular modulation frequency, and td =
delay of circuit (a function of instantaneous frequency). In this td = io + F(a&m pi),
8-28
FKEQUENCY MODULATION
Practical matters, such as ease of alignment, tolerance of manufacture, and adequate
selectivity, frequently dictate the use of undercoupled circuits in commercial f-m receivers,
thus resulting in a non-uniform amplitude characteristic. Even receivers designed to
have a flat selectivity curve are frequently in trouble as the result of spurious amplitude
modulation when the receiver is not accurately tuned or when the set drifts out of align-
ment. Thus it is desirable that the f-m detector system have fairly complete rejection of
amplitude modulation in order to reduce distortion.
The amount and type of harmonic distortion produced by the spurious amplitude modu-
lation is determined "by the manner of the detector response to it. As indicated by Figs.
9(6) and 9(rf) (p. 8-23), the response of the detector to amplitude modulation may be in
a balanced or an unbalanced manner, or a combination of the two. As shown here, by
Fig. 3, a receiver having a rounded-top selectivity curve, and correctly tuned, gives
predominantly third-harmonic distortion when the detector has a balanced response to
Detector
characteristic
with balanced
response to a.m.
j^7 Detector
y^S characteristic
// with '
^
unbalanced
;poase to a_m.
Frequency (A/)
+1.0
FIG. 3. Distortion from Ampli-
tude Modulation
FIG. 4. Amplitude Characteristic for Two Cascade
Double-tuned Transformers
amplitude modulation and gives predominantly second-harmonic distortion when the
detector has an unbalanced response to it.
The harmonic distortion can be calculated by writing the equation for the f-m detector
input-output characteristic in terms of both input signal frequency and amplitude. Then,
the equation for the signal amplitude vs. the signal frequency is found from the selectivity
curve. By considering the input signal to be frequency-modulated by a sine wave, the
resulting output from the detector can be written as a trigonometric series. Substitution
of suitable trigonometric expansions will give the fundamental and harmonic output signals.
As an example, consider a receiver with an i-f amplifier system including two coupled
circuit transformers having 0.7 of critical coupling and a band width such that the re-
sponse is down 6db at full system deviation (at ±75 kc for broadcast frequency modula-
tion). Figure 4 shows that the amplitude characteristic of such an i-f system can be closely
approximated by a parabola, giving: Ai — 1 — 1/2 (A/)2, where A/ = 1 corresponds to full
system deviation. Now the response of a balanced discriminator can be represented as
EG = A%k(Af), where A% is the applied signal amplitude, and k relates to the f-m detector
slope. If the amplitude modulation of the signal applied to the detector is effectively
reduced by some a-m reduction factor (a), then the amplitude modulation due to the i-f
selectivity is effectively reduced to A$ — 1 — - (A/)2. Then the detector output is:
£0=
~ \ (Af)-
fc (A/)
fc (A/) - £ J
(3)
Applying a sine wave of frequency modulation, A/ = sin pt (for lOOper cent modulation),
then.E© = k sin pt - ^& sin3 pi = k ( 1 - '-a) sinpZ -f — - sin 3pt, thus giving: Per cent
£ \ o / O
third-harmonic distortion * — — — -. For an a-m reduction factor (a) of 0.35, this
oU — */sa)
can be seen to give approximately 5 per cent of third-harmonic distortion.
CROSS-TALK AND BEATNOTE INTERFERENCE 8-29
It can be seen from the above that the exact amount and the harmonic order of the dis-
tortion will be affected not only by the selectivity and the manner and degree of the f-m
detector response to amplitude modulation but also by the alignment of the detector
relative to the intermediate frequency and by the tuning of the center frequency of the
f-m signal relative to the center frequency of the intermediate frequency. In particular,
it is possible to obtain regions of high audio output and large distortion when, as the signal
is detuned, the carrier level at the detector system falls below that necessary for good a-m
rejection and when the carrier, at the same time, is tuned on the steep side-slopes of the
i-f response. Such distorted side responses can be considerably reduced by using a rounded-
top i-f selectivity in conjunction with a well-designed ratio f-m detector.
10. DISTORTION DUE TO MULTIPATH RECEPTION
When the same radio signal is received over several paths having different delay times,
the several signals may combine to give increased or decreased amplitude and/ or an ad-
vance or delay in the resulting carrier phase. For fixed differences in time delay of the
paths, the relative phase of the signals will vary with frequency of the signal. Thus multi-
path reception of an f-m signal will result in spurious amplitude and spurious phase modu-
lation relative to the desired signal. The various signals can combine so that a substantial
null in transmission exists at certain frequencies. As the carrier deviates through such a
null frequency, a sudden downward amplitude modulation results in conjunction with a
rapid change in phase. The sudden change in phase can result in significant spurious
frequency modulation. It appears that, where multipath transmission is expected, it is
of primary importance that the f-m detector system have good a-m rejection, particularly
in terms of rapidity of action and amount of downward amplitude modulation that can
be accommodated. In general, the resulting f-m distortion cannot be eliminated; however,
a large amount of amplitude modulation is generally produced before such distortion is
severe. Thus, good a-m rejection helps considerably but cannot eliminate multipath dis-
tortion effects.
Although numerous examples of multipath transmission distortion have been cited on
the higher frequencies of 50 to 100 Me,* it does not appear to represent a serious threat to
the f-m broadcast industry. However, multipath transmission distortion virtually makes
voice communication by frequency modulation impractical on the long-distance short-
wave bands of 5 to 30 Mc.f The many paths of transmission occurring during "skip"
transmission on these frequencies result in the familiar selective fading frequently produc-
ing serious f-m distortion, particularly as the deviation is increased.
11. CROSS-TALK AND BEATNOTE INTERFERENCE
Interference in f-m systems may arise from other generated signals, such as communica-
tion f-m or a-m signals, either received directly or through spurious receiver responses, or
it may arise from noise signals of such form as fluctuation noise or impulse noise. The
response of an f-m system to such interferences is, in general, quite different from that of
an a-m system. For example, cross-modulation on amplitude modulation, where the
modulation of a strong undesired a-m signal produces amplitude modulation of a desired
signal, has no exact equivalent in an f-m system. The non-linearities which produce cross-
modulation in amplitude modulation produce some spurious signals in an f-m system which
can have the frequency modulation of both signals, but no direct cross-modulation of
one carrier modulation upon the other carrier is produced. $
If two carrier signals of different frequency exist in a linear system, the resulting signal
(see Fig. 5) has amplitude and phase modulation at the difference frequency rate. When
the ratio of the two signals is substantially different from unity, the fractional amplitude
modulation and the radian phase modulation are equal to the fractional signal ratio, that
is, the ratio of the weaker signal amplitude to the stronger signal amplitude. The average
frequency of the resulting signal, being the average number of cycles per second, is the
frequency of the stronger signal. Since the instantaneous frequency modulation is de-
termined by taking the differential of the phase modulation, the resulting signal has a
frequency modulation that is not only proportional to the signal ratio but also directly
* Frequency-Modulation Distortion Caused by Multipath Transmission, M. S. Corrington, Proc.
I.R.E., Vol. 33, 878 (December 1945).
t Observations of Frequency-modulation Propagation on 26 Megacycles, M. G. Crosby, Proc. I.R.E.,
VoL 29, 398 (July 1941).
J Two Signal Cross-modulation in a Frequency-modulation Receiver, H. A. Wheeler, Proc. I.R,E.,
Vol. 28, 537 (December 1940).
8-30
FREQUENCY MODtTLATION
composite signal
2 represent extremes
mplitude variations
1 a rid 83 represent extremes
of phase variations
When N small compared to C:
Peal- a.m. (as a fraction) ^i»-j
Peak phase modulation (radiar
i)w-g-~&
proportional to the frequency difference between the carriers. Thus, if the two carriers
are applied to an ideal f-m detector system, the average detector output will be determined
by the average frequency of the stronger signal and an f-m beatnote will occur in the de-
tector output ha\*ing a frequency equal to, and an amplitude proportional to, the differ-
ence in frequency between the carriers.
When the ratio of the two beating signals is far from unity, the a-m, p-m, and f-m beat-
notes are all substantially sinusoidal. However,
as the ratio approaches unity, the beatnote wave
forms depart from sinusoidal, as shown in Fig. 6.
In particular, the f-m beatnote approaches a pulse
wave form as the signal ratio approaches unity.
In an ideal f-m detector system, the detector re-
sponds only to the frequency modulation of the
stronger signal, resulting in substantially no cross-
talk from a weaker signal.* This applies to co-
channel as well as adjacent channel signals, if the
desired-to-undesired-signal ratio is measured just
preceding the circuit which effectively reduces or
which is effectively non-responsive to the amplitude
modulation of the signal. For co-channel interfer-
ence, an f-m beatnote, of variable frequency, re-
sults which has considerably less amplitude within
the audio spectrum (owing to the triangular f-m
beatnote spectrum as shown in Fig. 5) than
would exist in an a-m system. The direct
audible beatnote interference does not exist for
adjacent-channel interference in a conventional
f-m receiver.
In practical f-m receivers the ideal perform-
ance in regard to co-channel and adjacent-
channel interference is not realized because of inadequate a-m rejection. The amount by
which the signal ratio can approach unity is generally limited by the downward a-m rejec-
tion capability of the system. This generally means that the signal ratio can get to within
only 3 to 6 db of equality before cross-talk results, even with good f-m detectors. When
considering the signal-to-interference ratio for the adjacent channel case, the most adverse
condition during modulation must be taken. This exists when the undesired signal has
maximum deviation toward the center of the i-f pass band, and, owing to the sharp skirt
selectivity, this condition may differ considerably from the unmodulated case.
Another practical limitation results from Amplitude s~\ s~*\ /-Xv
inadequate rejection of superaudibie ampli-
tude modulation produced in adjacent-
channel interference, where the beatnote
generally exceeds 200 kc. The grid-bias
limiter plus balanced discriminator type of
f-m detector system suffers from this limi- a**^1^0" \S ^T
tation. The usual limiter grid-circuit and
diode load time-constants do not permit
following of the superaudibie amplitude
modulation, resulting in an effective unbal- modulation \^/ \^/ ~\~7 \~f"
ancing of the discriminator and a change in V V
average output of the limiter. This limita-
tion frequently requires a signal-to-inter-
ference ratio of about 20 db to eliminate
/o
Frequency of N (£)
FIG. 5. Addition of Two Carrier Signals
Phase *\
roodjuktton \
Frequency
modulation
s\
Vertical scale is actual modulation x -j-
FIG. 6. Beatnote Wave Forms
cross-talk from adjacent channel signals,
when this f-m detector system is used. De-
tector systems not including the equivalent of this time-constant limitation are generally able
to tolerate a 3- to 6-db signal-to-interference ratio to eliminate adjacent channel cross-talk.
12. FLUCTUATION NOISE INTERFERENCE
Fluctuation noise, such as thermal noise of resistive impedances, and shot noise and
imaiopitl noise of vacuum tubes, can be considered equivalent to a uniform spectrum of
* Coma«saClmiifteJ Interference between Two Frequency-modulated Signals, H. A. Wheeler, Proc.
IMPULSE NOISE INTERFERENCE
8-31
energy in which the components have random phase or timing. When the noise is small
compared to the signal, any individual noise component will beat with the carrier to give
an f-ni beatnote as illustrated in Fig. 5. Thus the resulting audio noise consists of pre-
dominantly high audio-frequency components giving a characteristic high-frequency hiss
for f-m noise as compared to the uniform spectrum with considerable low-frequency
rumble for a-m noise.*
To find the rms value of the audio noise, the output noise spectrum can be squared, the
resulting squared spectrum can be integrated over the audio band, and the square root
of the integral taken. Using this for the simple case of an audio system with uniform
response and sharp cut-oft, the f-m signal-to-noise ratio to the a-m signal-to-noise ratio
(called the f-m improvement ratio) is found to- be V§ fd/fa, when fa is the maximum audio
frequency and id is the maximum frequency deviation of the system. For 15-kc audio
and 75-kc deviation this gives an f-m improvement of 18.8 db.
By including a de-emphasis low-pass filter in the receiver, which is compensated for by
a complementary pre-emphasis circuit at the transmitter, the f-m signal-to-noise ratio
can be further improved. In this case the f-m signal-to-noise ratio including de-emphasis
to the a-m signal-to-noise ratio not including de-emphasis is given by:
fd
where /o is the frequency for 3-db attenuation of the de-emphasis filter. For broadcast
frequency modulation with 15-kc audior 75-kc deviation, and 75-microseeond de-emphasis
time constant (/o =* 2.12 kc), this gives an f-m improvement of 32 db.
The above relations are derived on the assumption that the noise is sman compared to
the carrier signal. In the region where the peak noise is almost equal to the peak carrier,
the simple relations are inadequate, and actually the f-m improvement is rapidly lost as
the signal is made weaker. The approximate threshold for f-m improvement is when the
peak carrier equals the peak noise.
Signal-to-noise ratios are frequently expressed in terms of the rms audio signal output
for 30 per cent frequency modulation to the rms audio noise when the carrier is unmodu-
lated. Using this definition and applying the approximate equa-
tions at the f-m improvement threshold (where peak carrier
equals peak noise after selectivity), the signal-to-noise ratio for
broadcast frequency modulation with 150-kc i-f pass band is
about 40 db at the threshold. Thus, in this case, the frequently
used 30-db signal-to-noise ratio is near the knee of the improve-
ment threshold, and when the receiver has good a-m rejection
it is determined by the signal level which approximately gives
peak carrier equal to peak noise. For broadcast f-m receivers
with 150-kc i-f pass band, a 300-ohm antenna, and an assumed
receiver noise factor of 6 db, the threshold level (peak carrier =
peak noise) is at about 104 db below 1 volt. This would repre-
sent a very well-designed set. Normal design receivers have
an improvement threshold around 90 to 100 db below 1 volt.
When the peak carrier greatly exceeds the peak noise, the
signal-to-fluctuation-noise ratio of an f-m system is improve*d by
using a larger deviation ratio. However, a small-deviation-ratio
system can have narrow receiver selectivity resulting in less total peak noise and thus
a lower threshold signal level, as illustrated in Fig. 7. Thus, entertainment f-m systems
where signal-to-noise ratio is important are built using a large deviation ratio, while com-
munication networks where range of coverage is important use a small deviation ratio.
Signal input
FIG. 7. Small- vs. Large-
deviation Ratio FM
13. IMPULSE NOISE OTTEBEERENCE
When an impulse, such as automobile ignition interference, is applied to a receiver, a
transient carrier pulse results having a duration determined by the band widthf of the
receiver and a frequency determined by the center frequency of the i-f selectors. When
this transient is added to a desired carrier, an amplitude and phase modulation of the
desired carrier results, depending upon the relative amplitude, frequency, and phase of
the carrier and the transient. If the carrier amplitude is larger than the peak amplitude
* Frequency-modulation Noise Characteristics, M. G. Crosby, Proc. I.R.E., Vol. 25, 472 (April 1937).
8-32
FREQUENCY MODULATION
Phase pufse
("click")
Phase step
("pop")
Signal (Ec) plus
impulse (Ej)
vectors
Phase
modulation
Frequency
modulation
JL
4-
of the transient, the maximum phase modulation that can result is a pulse of less than
1 radian. In this ease the audible interference produced, particularly in large-devmtion-
rain' t'hfcS'ot mecS interest, which occurs very frequently, the transient impulse ampli-
tude greatly exceeds the carrier amplitude. If the desired carrier has a frequency equal to
the center frequency of the selector, then the transient and the carrier have a fixed phase
during anv one pulse. This results in a pulse of phase modulation which can have a max-
imum phase displacement of approximately 180° when the transient and the desired car-
rier are almost out of phase. .
If the desired carrier has a frequency different from the center frequency of the selector,
then the transient and the carrier will slip in phase between the beginning and end of any
one transient pulse. For certain con-
ditions of starting phase, this case will
still result in a pulse of phase modu-
lation as shown in Fig. 8. However,
there are certain conditions of starting
phase such that the resulting signal
vector snaps back to its original phase
after going through 360° of phase dis-
placement during the pulse (see Fig.
8). This produces a step of phase
modulation instead of a pulse of phase
modulation. Thus, when the desired
signal is not exactly on tune either a
pulse or a step of phase modulation
can result from a strong impulse noise,
with the probable occurrence of the
phase step becoming greater as the
signal is further detuned.
When a phase pulse is applied to
an ideal f-m detector, the output sig-
nal is a double-polarity pulse. This
double-polarity pulse applied to the
de-emphasis filter and audio system
results in a unipolarity pulse having
relatively little energy and a short
duration determined by the cut-off
frequency of the audio system. This
weak audio output noise is sometimes
called a "click." When a phase step
is applied to an ideal f-m detector a unipolarity pulse results. This pulse applied through
the de-emphasis filter and audio system gives a pulse with an exponential decay deter-
mined by the de-emphasis time constant and thus having relatively more audio energy.
This louder audio noise is sometimes called a "pop.** *
Thus, when a strong impulse is applied to an f-m receiver, either a noticeable pop or
weak click may result in the audio output, with the probable occurrence of the "pop"
being directly related to the detuning of the desired carrier relative to the center frequency
of the selector. In broadcast* f-m with 75-kc deviation and 75-microsecond de-emphasis
time constant, the click may have a peak amplitude between zero and about 6 per cent
of full modulation, and the "pop" will have a peak amplitude of about 18 per cent of full
modulation. The amplitude and probability of occurrence of the pop is almost independ-
ent of the amplitude of the impulse after it exceeds the carrier level by several times.
To obtain the performance described above, the f-m receiver must have good a-m rejec-
tion; otherwise the large amplitude modulation resulting from the impulse noise will be
heard. Also, care must be taken to see that the receiver recovers immediately after a
strong impulse; otherwise the absence of a signal immediately after an impulse may result
in a large audio output due to inadequate downward a-m rejection. This trouble can
result particularly in a grid-bias limiter with an improper grid time constant. Another
limitation preventing ideal performance can be spurious phase modulation produced
within the receiver, during the impulse, from such causes as change in input capacity of
amplifier tubes.
* The Theory of Impulse Noise in Ideal Frequency-modulation Receivers, D. B. Smith and W E
Bwufley, Pr&c. I.R.E., Vol. 34, 743 (October 1946).
Audio
output
Time — >• Time —
FIG, 8. Impulse Noise Interference
SECTION 9
PULSE TECHNIQUES
PULSES AND PULSE SYSTEMS
AET BY HAROLD A. WHEELER PAGE
1. Introduction 02
2. Comparison of Continuous Waves and
Pulsed Waves 02
3. Types of Pulse Modulation 03
4. Speed of Information. 03
5. Communication 05
6. Picture Transmission 06
7 Computers 08
8. Distance Measurement 09
9. Pulse Measurements 10
PULSE CIRCTnTS
ART. BT J- J- OKRENT PAGB
10. Frequency Multipliers, Dividers, and
Counters 13
11. Pulse Amplifiers , 14
12. Pulse Shaping Circuits 15
13. Relaxation Circuits 17
14. Pulse Timing Circuits 19
15. Pulse Modulation of an Oscillator 21
16. Modulating the Characteristics of Pulses 23
17. Pulse Detectors 24
18. Vacuum Tubes 26
19. Pulse Transformers 27
BY HAROLD A. WHEELER
20. Delay Lines 28
9-01
PULSE TECHNIQUES
PULSES AND PULSE SYSTEMS
By Harold A, Wheeler
1. INTRODUCTION
The various uses of pulses in signaling and measurements were greatly advanced during
World War II with the advent of numerous devices for aiding navigation, -detecting and
locating enemy craft, and performing difficult measurements and computations. It is
the purpose of this section to give a broad perspective on the many applications of elec-
tronic pulse techniques and their limitations, together with a few of the more common
circuits and a large bibliography for further reference.
Pulse coding is exemplified by the time-honored telegraph codes, which were originally
operated slowly enough for crude mechanical devices, manual transmission, and auditory
reception. Electronic pulse techniques were adapted to -code systems for amplifying weak
signals and expediting the various processes.
Pulsed radio waves date back to the original spark transmitters of Hertz and others,
which set the pattern of early radio communication. With the obsolescence of spark
transmitters began the evolution of electronic pulse transmitters, which had their greatest
use in "radar" during the war. They now develop as much as a megawatt of pulse power
at frequencies around 3000 megacycles (wavelength 10 cm) . In some cases, the old rotary
spark gap has been revived to key the new magnetron pulse transmitters.
2. COMPAMSON OF CONTINUOUS WAVES AND PULSED WAVES
Various kinds of information, such as voice or music, are transmitted by corresponding
modulation of a carrier wave. (See Section 5, Transients in Networks, and Section 17,
Telephone Systems.) In the simplest form, the carrier is a continuous wave of a fixed
frequency, and its amplitude is modulated in accordance with the sound wave or other
information to be transmitted. Amplitude modulation is unique in that the modulated
wave can be transmitted within the narrowest bandwidth in the frequency spectrum.
Other forms such as frequency modulation and pulse modulation require excess bandwidth
but in return they secure some advantages which may justify the cost in bandwidth.
The continuous waves used in amplitude or frequency modulation on one hand, and
pulsed waves on the other hand, have entirely different properties which require different
points of view in their application. These differences are most pronounced in the selection
of one signal out of several signals or noise of comparable amplitude.
Figure 1 shows the principles of selection between two signals, regardless of their relative
amplitude. As modulated continuous-wave signals are coextensive in time, frequency
selection must be used for each channel
-First channel by means of band-pass filters. Pulsed
* j — Second channel signals, however, can be separated in
r~ Harmonic of second channel time, and so it is possible to use time
S~ ~"\ selection as well as frequency selection
\ for filtering one channel from another.
Frequency or time ^ The. "skirt ^k^^y" ^ frequency se-
lection denotes the attenuation just
FIG. 1. Selection in Frequency or Time outside the desired frequency band; in
time selection it denotes the rate of
damping of one pulse to clear the way for the next pulse of another channel. Frequency
selection is subject to harmonic interference, as shown in dotted lines in Fig. 1; the anal-
ogous interference in time selection is caused by pulse echoes in the transmission paths
in enclosed circuits or open space.
In any system including several signals with the same form of modulation, some severe
requirements have to be met in order to avoid interference between signals. Continuous-
9-02
SPEED OF INFORMATION
9-03
wave signals require that the response be very nearly linear in order to avoid harmonic
interference or cross-modulation of one signal by another. This is not a requirement for
pulses separated in time, because they are not coexistent. Instead, the pulse signals
require that each pulse be damped out immediately after its occurrence and that later
echoes be avoided.
The rating of equipment for pulse modulation places the emphasis on peak values rather
than average values. For example, small vacuum tubes can be made to tolerate high
peak values of current and voltage if they occur during only a small fraction of the time.
Accumulative effects, such as heating and the decomposition of the glass, become less
important because they depend on average values.
(&) Width (duration)
n _ ru
) Spacing (phase, frequency)
FIG. 2. The Three Basic Types of Pulse Modulation
.
3. TYPES OF PULSE MODULATION
The many possible ways of modulating pulses involve three basic types of modulation
as illustrated in Fig. 2. Height modulation (a) corresponds to amplitude modulation of
a continuous wave. Width
modulation (6) and spacing
modulation (c) involve only
the time dimensions and are
therefore not critically depend-
ent on the pulse amplitude.
The greatest advantages of
pulses are realized in time mod-
ulation (£>) or (c) as distin-
guished from amplitude modu-
lation (a) in Fig. 2. The tele-
graph codes are an example of
width-and-spacing modulation.
It is permissible to use ampli-
tude clipping or limiting cir-
cuits, since the amplitude need
not be preserved. Also the de-
tectors are made responsive to timing and can be made unresponsive to amplitude fluctua-
tions such as power-supply ripple.
Pulse echo systems, such as radar, utilize the timing of the echo to determine the dis-
tance. Some pulse systems use directive antennas which receive alternately on two crossed
lobes of the directive pattern. In this case, the relative amplitude of echo pulses must be
preserved and the direction of reception is observed at the intersection of the two lobes
by equalizing the echo-pulse amplitudes.
Some kinds of information, such as numbers, can be transmitted by grouping together a
number of pulses in succession. Each group can be evaluated by a pulse counter. Mul-
tiple-pulse coding is essentially similar to pulse-width modulation but has some advantages
in handling and in reliability of decoding.
The modulation of pulses of uniform width is similar to the modulation of a subcarrier,
which in turn modulates a carrier. The pulse frequency is intermediate between the
modulation frequencies and the carrier frequency, as is a subcarrier frequency. In the
case of pulses, however, several sets of short pulses of the same frequency can be super-
imposed for multiplexing simply by displacement in time, whereas each continuous-wave
subcarrier would need a different frequency. The pulse pattern can be subjected to any
method of modulation applicable to a carrier or subcarrier, notably amplitude modulation
as in Fig. 2 (a) and phase or frequency modulation as in Fig. 2(c).
4. SPEED OF INFORMATION
A time variation of a quantity (such as current or voltage) may be regarded as comprising
a succession of contiguous pulses of varying amplitude (see Fig. 4, p. 5-28) . The speed of
information that can be transmitted through a signal channel by such a variation may be
conceived as the maximum frequency of such pulses whose presence or absence can be
individually detected. (A space is regarded as an absent pulse, or one of zero amplitude.)
Therefore the speed of information is limited by the frequency bandwidth. In the case
of a low-pass channel (or one-half of a double-sideband band-pass channel), the nominal
minimum bandwidth is one-half the maximum pulse frequency as here conceived, but
somewhat greater bandwidth is needed for insurance of pulse damping and for skirt
9-04
PULSE TECHNIQUES
selectivity against adjacent frequency channels. Figure 3 shows the nominal bandwidths
required for a speed of information equal to 2/c. (The maximum pulse frequency as here
used is twice the maximum frequency of discrete pulses separated by intervening spaces of
equal width; for those separated pulses
the nominal minimum bandwidth be-
comes equal to the pulse frequency.)
The foregoing relation is based on
the assumption of adjacent non-over-
lapping pulses, although some overlap
is permissible in practice. The particu-
lar needs of the system determine how
7"!
Augmented bandwidth
Minimum bandwidth
I
1
I
! i
G. 3. Frequency Bandwidths Required for a Certain
Speed of Information
(a)
(6)
0 fe Frequency f0-fe-* f0 W0 +/e
much the actual bandwidth must exceed
the nominal minimum bandwidth. Fig-
ure 4 shows the distortion of a discrete
square pulse which is caused by reduction of system bandwidth.
In Fig. 4 the square pulse (a) represents the voltage pulse or the current pulse produced
by a system with a very wide bandwidth. In the remaining cases the nominal bandwidth
of the system (/c) is successively reduced to show its effect on the output pulse caused by a
square input pulse. Case (6) shows a system bandwidth (fc) approximately four times
that of the nominal pulse bandwidth. This limitation causes sloping sides but retains a
flat top over part of the pulse width. In (c), the system bandwidth is reduced to twice
the nominal pulse bandwidth, just leaving a peak at the original amplitude. A system
bandwidth equal to the nominal bandwidth of the square pulse (d) leaves the pulse
slightly reduced in amplitude and considerably widened. Further, halving of the band-
width (e) reduces the amplitude of the output pulse to less than one-half of the value in (a)
and increases the width to more than double. Cases (c) or (d) may be regarded as practical
compromises.
Like frequency modulation or subcarrier modulation, pulse modulation unavoidably
increases the bandwidth requirements for the same speed of information, in the manner
of the augmented bandwidths indicated by dotted lines in Fig. 3. The greater bandwidth
inherently increases the average power of background noise caused by thermal agitation
of electrons. It also makes
possible a proportional in-
crease in the peak power by
pulsing, while maintaining
the same average power.
If the signal amplitude is
comparable with the noise
amplitude, a change to puls-
ing with its greater band-
width is no advantage. If
the signal is somewhat
stronger than the noise,
however, and if the pulses
are modulated in time, it is
found possible to secure an
advantage in signal-to-noise
ratio which is comparable
with that obtained in wide-
band frequency modulation
over the same bandwidth.
Therefore, if the augmented
bandwidth is available, pulse
modulation is another way
to take advantage of it.
It may happen that, for
some reason, more band-
width is available than the minimum needed for the desired speed of information. At
very high frequencies, the accidental frequency fluctuations of the signal may require an
augmented bandwidth in tbe receiver. £ome of this excess bandwidth may then be utilized
t0 advantage by pulse modulation.
FIG. 4.
The Widening of a Square Pulse by Reduction of Frequency
Bandwidth
' — Time
COMMUNICATION 9-05
5. COMMUNICATION
The various types of pulse modulation have long been used in low-speed and high-
speed code transmission of word messages (see Sections 17 and 18, Telephony and Teleg-
raphy) , but the greatest advance in pulse techniques has been utilized more recently in the
multiplex transmission of several voice channels on a single microwave beam as a carrier.
This system is taken as an example of the communication possibilities with .pulse modu-
lation.
The carrier is modulated in short pulses, and the pulse spacing is modulated by sound
waves. This is the type of modulation shown in Fig. 2(c) above. The multiplex operation
is accomplished by interspersed pulses as shown in Fig. 5. A single group of pulses com-
prises a sequence including one
pulse assigned to each channel. 1234 1
One channel is reserved as syn- ' ' *"* ~ "~
chronizing pulses to initiate each
counting sequence in reception.
Each of the remaining chan- FIG. 5. Multiplex Operation of Several Channels by Pulse-time
nels is modulated by shifting Modulation
its pulses in time in accordance
with the sound wave to be transmitted. The amount of time modulation of each pulse is
limited so that the modulation of one pulse will never encroach on the time allotted to the
modulation of the adjacent pulses.
In the transmitter, the pulses belonging to each channel are synchronized by the first
channel but are otherwise separately generated and modulated. Then all channels are
combined with pulses interspersed, and the composite pulse pattern is used to modulate
the carrier wave.
In the receiver, the modulated carrier wave is amplified and detected, then each sequence
of pulses is distributed among the several channels under guidance of the synchronizing
pulses of the first channel. The distribution of each sequence may be accomplished by
some form of counting or tune selection. As long as the successive pulses are separated
in time, there is no interference between channels. The time selection of multiplex
channels offers some advantages over frequency selection, unless there are strong echoes
with enough delay to overlap succeeding pulses, a condition that can be avoided by highly
directive beam transmission.
Reliable reception is generally possible if the desired pulse peaks are received somewhat
stronger than the peaks of noise or other interference. By amplitude limiting and clipping,
the pulse peaks are flattened and the lower parts of the pulses (in the noise background)
are discarded. The result is a succession of square pulses with the same timing as the edges
of the received pulses. These reconditioned pulses are distributed to the separate channels
for recovery of the modulation.
Since the sides of each pulse are sloping, the timing of the reconditioned pulse is still
subject to some disturbance by background noise, as illustrated in Fig. 6. The noise causes
some vertical displacement of all parts
of the pulse, while there is no change
in the level which determines the recon-
ditioning and subsequent detection.
- Detection level Therefore the vertical displacement is
translated to a minor amount of time
. Time displacement, always less than the pulse
width. The time modulation caused
FIG. 6. Pulse Detection with Background Noise b^ noise may be compared to the avail-
able time modulation by the signal, to
determine its disturbing effect. Increasing the frequency bandwidth proportionately in-
creases the slopes and thereby decreases the response to background noise (as in wide-band
frequency modulation) . Increasing the available time width for modulation (as by decreas-
ing the number of channels) decreases the ratio of the noise modulation to the signal
modulation.
The ultimate effect of the noise on the pulse slopes in Fig. 6 depends on the- kind of
detection. The simple detectors of time modulation operate on one edge of every pulse,
either the leading or the trailing edge. Such detection retains the full effect of the back-
ground noise on the sloping edge of each pulse. The time detection may be designed to
operate on the center of the reconditioned pulse, in which event there is approximate
cancellation of those noise components that merely shift the pulse up and down, as illus-
9-06 PULSE TECHNIQUES
trated in Fig. 6, leaving only the effect of those components that distort the shape of the
pulse. The choice of the kind of detection depends not only on the noise but also on other
factors which may be more important.
A common form of interference in pulse transmission is echoes caused by reflection of
waves from objects in space or from irregularities in transmission lines. In communica-
tion between aircraft, the principal cause of echoes is ground reflection. Figure 7 shows
how an echo may distort the trailing edge of a pulse. A direct pulse is interfered with by a
slightly later echo pulse (shown in
dotted lines) which is considerably
weaker (below the detection level).
The diagram shows only the envelope
Detection level of the puised wave. As the relative
—7
/
-^ --- "
>~
phase of the carrier wave of the two
Y — ^3» Time pulses may have any angle, the echo
V"** may add or subtract on the trailing
FIG. 7. Pulse Detection with Echo edge, as shown. Between fixed trans-
mitter and receiver, the effect of the
echo is fairly steady, varying slowly with frequency drift and environment; therefore it
contributes little or no disturbance in the receiver. If the distance is variable, as be-
tween aircraft, the relative phase of the two pulses varies at random, and so an echo
causes noise if the time detection operates on the trailing edge.
Pulsed waves are most commonly obtained by pulse modulation of a carrier-frequency
oscillator which delivers the required power directly to the antenna. At the beginning
of each pulse, the oscillation has to build up from the noise level. Therefore the oscillator
acts as a superregenerative amplifier of the background noise. The resulting noise on the
leading edge of the pulse is illustrated in Fig. 8. The modulator pulse is shown in dotted
lines. At the beginning of the modulator pulse, the oscillation starts to build up expo-
nentially from the noise level and soon reaches equilibrium at the power level of the oscil-
lator. However, the fluctuation of the noise causes a variable delay in the build-up of
successive pulses, which appears as a "jitter" in the leading edge. If the time detection
operates on the leading edge, the re-
sult is noise in the receiver. This
effect is absent on the trailing edge
because the latter is determined by -- 1 -- -?/? --- ^\ ---- Detection level
exponential damping from the stable
level of the oscillator on the peak of - 1-^2^ --- ^ - Time
the pulse. (The noise on the leading FIG. 8. Output Envelope of Pulsed Oscillator
edge can be avoided if the pulse
modulation is applied to an amplifier following a continuous carrier-frequency oscillator,
but this method has other disadvantages.)
The use of a very short pulse, shifted in time with modulation, appears to be the most
economical of power while realizing the advantages of pulse modulation. The pulse dura-
tion should be nearly the least that can be transmitted within the available bandwidth
in the frequency spectrum. Then the available average power can be utilized to secure
greatest pulse amplitude for overcoming noise. Since the detection operates on the edges
of the pulses, greater pulse duration is no advantage and greater amplitude is a propor-
tionate advantage.
Detection on the leading edge, the pulse center, or the trailing edge, is a choice that
depends on the nature of the system. In beam transmission along a fixed path, echoes are
unlikely, so detection on the trailing edge is preferable to avoid the oscillator noise on the
leading edge. Broadcast transmission, especially between moving stations, is subject to
echo interference, which gives the advantage to detection on the leading edge; the oscillator
is then designed to minimize the superregenerative noise. If both the echoes and the
superregenerative noise are less than the random background noise, center detection
would give the best performance and its complication might be justified.
The potentialities of multiplex pulse transmission are indicated by the studies which
sfeow that the entire broadcast services for a large city could be transmitted from a single
microwave system centrally located on the highest building, with a service area limited
by tfase optical horizon.
6. PICTURE TRANSMISSION
I® picture transmission by scanning methods (see Section 19, Facsimile, and Section 2Q,
km), pulses are relied on not only for reproducing the picture elements but also for
and synchronizing the scanning process. Since the common systems for picture
PICTUEE TRANSMISSION
9-07
transmission utilize scanning methods, many examples of pulse circuits and their applica-
tions are found in both facsimile and television.
Figures 9 and 10 show respectively the essential components of a picture transmitter
and receiver with scanning by deflection of an electron beam, as in present-day television.
Line
Carrier
frequency
frequency
oscillator
oscillator
t Sy
Line
" sawtooth
<-
Line
frequency
pulse
->
Line sync,
pulse
Camera
generator
generator
generator
tube
J,Sc
^Sy
Sy
Picture
Retrace
*
Picture
->
signal *•
block-out
pulse
Frequency
divider
Mixer
->
Modulator
— > Antenna
generator
generator
r
P
P
Sc
t
4 Sy
Sv'
- p
Sy P Sy P
Frame
Frame
Frame
- sawtooth
4-
frequency
pulse
sync,
pulse
I
Sc
Sy
Sy
Picture
signal
amplifier
FIG. 9. Block Diagram of Picture Transmitter
r
Line
sawtooth
generator
J*
Picture
tube Projector
Antenna
Carrier
selector
Det
Sync.
Picture Picture
Sc
and
amplifier
separator — [
reproducer image
Frame
sawtooth
generator
P Sy
P Sy P
Sy Sy U
Sc'
* P P
Sc
Picture
amplifier
FIG. 10. Block Diagram of Picture Receiver
In these block diagrams, the various functions are coded:
P = picture channel.
Sc — scanning functions.
Sy — synchronizing functions.
The picture signal is generated in the transmitter and converted back to an image in
the receiver. The scanning function is individual to tra.nsTn.it.tftr or receiver. The auto-
matic synchronizing operation is initiated in the transmitter by the liae-freojiency oscillator
and used directly to time the scanning in the camera tube; it is. maintained by transmitting
timing pulses along with the picture signal, which are selected in the receiver for holding
in step the scanning in the picture tube.
Figure 11 shows an example of the pulses involved in the scanning of a single horizontal
line in a picture. This line is located at the dotted line in the pattern (a). The graph, (6)
shows in the period P the picture signal for the line. As the scanning line crosses the
circular line, a black pulse is generated; as it crosses each edge of the black disk a step is-
9-08
PULSE TECHNIQUES
(a)
generated, two steps making a wide pulse. The line signal is preceded and followed by a
synchronizing pulse Sy which times the successive lines. The sync pulse is communicated
at an "infra-black" (blacker than black) level and so it does not appear in the retrace
lines back across the picture between lines. The graph (c) shows the sawtooth wave of
voltage or current which is used to deflect the cathode ray or electron beam, in the camera
tube or picture tube, from one end of the line to the other. , , .
The transmission of the picture involves the communication of many pulses, each having
an amplitude proportional to the brightness of a small element of the picture. The "speed
of information" may be expressed as the number of "independent" picture elements that
can be transmitted per second, or the number of pulses per second. It ranges from hun-
dreds in facsimile up to millions in
television. Completely independ-
ent transmission of adjacent pic-
ture elements by successive pulses
is never attained because the elec-
trical circuits and other devices
cause distortion resulting in over-
lapping of adjacent pulses. One
of the principal problems is there-
fore the design of the circuits to
reproduce the short pulses with
clean edges by minimizing ampli-
tude and phase distortion over
the requisite frequency bandwidth
in the circuits. Both kinds of dis-
tortion are usually more prevalent
at frequencies near the limits of
fc\ the frequency band required for
reproduction of the pulses and
lme steps. The higher frequencies play
the major part in reproducing
vertical lines or edges; the lower
frequencies, in reproducing long
pulses or background.
* "«
is
§
Levels
Sync. —
FIG. 11. Example of Pulse Functions in Picture Transmission
The basic timing of the system depends on line-frequency pulses generated in the trans-
mitter (Fig. 9) in step with a line-frequency stable oscillator. These pulses are used directly
to synchronize both the horizontal line scanning in the camera tube and the sync pulses
in the composite signal. By means of frequency dividers or pulse counters, one of these
pulses is selected at the proper time to interrupt the vertical scanning at the end of each
frame. The resulting frame-frequency pulses are used in a similar manner to synchronize
the vertical scanning.
The synchronizing pulses need to be specified and preserved in shape only to the extent
required by precision of timing in the scanning operation. Since they are selected from
the signal at a certain infra-black level which may fluctuate with picture content, it proves
necessary to hold the edge of a sync pulse nearly as steep as the edge of a step in the picture
signal. As sync pulses need not be modulated in amplitude, they can be subjected to
limiting or clipping action to remove accidental changes in amplitude. A practical tele-
vision system may have rather complex sync pulses for facilitating the separation of line
and frame sync signals, and for minimizing their susceptibility to interference from the
picture signal or other disturbances.
7. COMPUTERS
The solution of certain problems, such as the trajectory of a missile, requires elaborate
calculations, which are laborious even when done on mechanical computing machines.
Electronic computing machines can increase the computing speed by a factor of 1000 or
more, so that a compilation of tables which would take years on a mechanical computer
would be done in a few hours or days on an electronic computer. The addition of a digit
in electronic computing requires a few microseconds as compared with a few milliseconds
in mechanical computing.
Aa outstanding electronic computer is one of the products of World War II, the "elec-
tronic numerical integrator and computer" (eniae).
An electronic analog of the mechanical counter or electromechanical stepping relay
may be made up of a number of flip-fiop relaxation circuits connected to be switched con-
DISTANCE MEASUREMENT
9-09
secutively by successive pulses. A single flip-flop circuit is analogous to a toggle switch,
snapping from one condition to the other and remaining there until an external force snaps
it back. In the block diagram of a two-digit ring counter, Fig. 12, each input pulse snaps
the "on" switch "off" (to the left), which in turn snaps the next above switch "on" (to
the right), increasing the indicated number by one. If the units column indicates nine,
and a unit is added, the units "nine" switch is snapped off, the units "zero" switch is
snapped on, and the tens column receives a pulse, increasing its indicated number by one.
In the eniac, when going from "nine" to "zero," a "carry" switch stores the pulse for the
next column. Simultaneous addition in all columns is thereby made possible. The
"carry" switch is snapped off after addition in the columns is complete.
An electronic computer may consist of the following:
1. A number of counters to add and store numbers represented by pulse groups.
2. A generator of suitably timed standard pulse signals.
3. Devices for converting numbers supplied to the computer into pulse groups repre-
senting the numbers.
4. Devices for printing numbers stored in counters.
5. Devices for combining the quantities in the counters in different ways to add, mul-
tiply, divide, etc.
6. Devices to produce automatic repetition of required computations, as in numerical
integration.
A basic decade ring counter was described above. The decade counter may be so
arranged that, when supplied with a standard
sequence of pulses from the timing generator,
a number of pulses corresponding to the number
stored in the counter is transmitted to another
counter which adds it to its own stored number.
Various groups of pulses from the timing gen-
erator may be selected and combined by switch-
ing to produce pulse groups corresponding to
numbers to be supplied to the computer. The
numbers stored by a counter may be indicated
by neon lamps energized by "on" flip-flops, as
indicated by the black dots in Fig. 12. Card
punching or printing devices may be similarly
actuated to record a stored number.
Rapid switching is accomplished by means of
triple-grid tubes, keying pulses being applied to
one control grid and information pulses being
transferred via another control grid.
The flexibility of an electronic computer as
regards physical location of components, num-
ber of interconnections possible, and the large
tolerances in amplitude possible, facilitates the design of computers to perform very
elaborate computations with lightning speed.
Where absolute numerical precision is not required, the step counter may be replaced
by simpler devices relying on continuous integration. In one type, each pulse delivers an
incremental charge to a capacitor whose stored charge is indicated on a meter scale. In
another type, the pulse rate is indicated by conducting the incremental charges through a
d-c meter so that the current is proportional to the number of pulses per second. Examples
of these types are found in Geiger counters, long in use for recording pulses of radioactive
radiation.
8. DISTANCE MEASUREMENT
Distance can be measured by timing pulses transmitted through a medium in which
the wave velocity is known. In the interest of precision, the duration of each pulse
should be much less than the time required for the wave to cover the distance in question.
The three basic methods used in operating systems are described in Section 22.
Diverse Waves. Observations of distance by this principle are based on the reception
of a pulse by two kinds of waves, over the same distance, having different velocities so
that the time difference in reception is a measure of the distance. Examples of light and
sound waves originating in simultaneous pulses and traveling over the same distance are
found in lightning and thunder or in the seeing and hearing of a distant steam whistle.
In these cases, the only appreciable delay is in the sound wave, and so the computation
of the distance is based on the velocity of sound in air. An example of different types of
Units
Two-digit Decade Counter
input
9-10
PULSE TECHNIQUES
waves in the same medium is given by the seismograph of an earthquake. The pulses
are transmitted through the earth by longitudinal waves (pressure waves, like sound)
and transverse waves, having different known velocities so that the difference in time of
reception permits computation of the distance. (See Section 22, article 9.)
Pulses from Diverse Locations. One of the outstanding radio navigational systems
(loran, gee, and shoran, Section 22, article 10) also utilizes pulses spontaneously transmitted
to the observer, but from widely spaced points and carefully synchronized in time. The
time difference in their reception by radio waves permits precise computation of the differ-
ential distance relative to each pair of spaced points, and such observations on two different
pairs determine the position of the receiver.
Reflection or Return of Pulse. The more versatile systems employ pulse waves trans-
mitted from the observer to a distant point and back again to his receiver. The elementary
Table 1. Wave Velocity
Kind of Wave
Medium.
Velocity
Electromagnetic (light, radio)
Sound . . .
Free space (and air)
Air (atmospheric pressure, 20 deg C)
300 m/ps
344 m/sec
Sound . ... .
Water (20 deg C)
1464 m/sec
Seismic (longitudinal, sound) ....
Seismic (transverse)
Earth
Earth
4- 14 km/sec
3- 10 km/sec
sonar and radar systems utilize short pulses of sound or radio waves transmitted toward
an object and reflected back to a receiver (Section 22, article 10) . Special radar systems
for beacons or identification rely on a pulse repeater at the object, which receives and re-
transmits the pulses with coding of some kind (radar beacons, Section 22, article 10; and
Lanac, Navar, and Teleran, Section 22, articles 6 and 11). In any case, the round-trip
time at known velocity determines
Table 2. Characteristics of Radar tne distance.
Table 1 shows various values of
the wave velocity in different me-
diums. Table 2 shows the ap-
proximate range of pulse charac-
teristics in radar systems of the
reflection type. Since the error of
time measurement may be reduced to a fraction of the pulse width, the corresponding
distance error may be reduced to the order of 1-0.01 mile. The range of echo reception
varies from a few miles to above 200 miles.
Carrier frequency , ...
30-30,000 Me
Carrier wavelength
1 0-0 . 0 1 meters
Pulse width
1 0-0 25 tis
Pulse repetition frequency
60-4,000 cps
Pulse power
10-1,000 kw
9. PULSE MEASUREMENTS
PULSE AMPLITUDE. A simple pulse of voltage or current can be displayed on an
oscilloscope and its various properties determined from the calibration of the scope. Such
a display is shown in Fig. 13. The small pulses or
"pips" are superimposed marker pulses carefully
timed to provide a time scale. A representative
scale might have small marker pips every micro-
second, and every fifth one enlarged. In Fig. 13 the ' f * * ' ' \1 t t 1 t r i r | TJme
pulse under observation is 1 division wide at the FIG. 13.
peak and about 2 divisions at the base; it might be
rated 1.5 divisions wide at half amplitude.
Oscilloscopic Observation of
Pulse Characteristics
A pulsed wave having many cycles of the carrier in a single pulse presents a special
problem if the scope cannot give a calibrated display of the actual carrier cycles. The wave
must be rectified for display, and the performance of the rectifier is difficult to predict or
measure. If the rectifier responds quickly, the rectified pulse may be displayed as in Fig.
13, which is adequate for observing its width or duration.
An indirect method is usually employed for rough measurement of the amplitude of a
repeating pulsed wave, the pulse power, for example. The average power is measured by a
thermal device such as a thermocouple or bolometer. The pulse duration is observed as
in Fig. 13. Then the ratio of peak to average power is equal to the ratio of the period of
repetition to the pulse duration. This method is accurate if the time occupied by the sides
of the pulse is much less than the duration of its peak. Otherwise the pulse width is
indefinite, usually approximated by the width between the points at one-half the
Tjme
PULSE MEASUREMENTS 9-11
power or the peak amplitude. (This same method is applicable to simple pulses if there is
no background of direct current or voltage, but it is not usually needed in this case.)
In the case of a pulsed carrier wave, some care is required in expressing the peak values
during the pulse. The peak power is the mean power of the carrier wave at the peak of
the pulse. If there are minor ripples on the flat top of a pulse, the pulse power is stated at
the level of the flat top. The peak voltage may be stated as the peak value of the carrier
voltage at the level of the peak or flat top, since that is the value significant for voltage
breakdown. The pulse current in a vacuum tube carrying a pulsed wave is usually stated
as the average value of the current during the peak or flat top of the pulse, since that is
the value readily measured by means of an oscilloscope.
The pulse amplitude of a pulsed wave is best measured by comparison with a continous
wave of known amplitude, since such a wave presents no unusual problem. The "notch"
method shown in Fig. 14 is based on this principle.
The comparison wave is cut off or notched for the i / \ r "
duration of the unknown pulse. Then the pulsed \ / \ /
wave is superimposed thereon, and the composite i__]L
wave is rectified and displayed on the scope. The Fl<}_ ^ Mca8Urement of Pulse ^
two amplitudes are equalized, to give tne appearance tude by Comparison with Continuous
of Fig. 14; then the pulse amplitude is known. This Wave
method is independent of the rectifier and scope
characteristics and has been found very useful. Measurements have been made as low as
200 MW peak pulse power and 2 /zw average power.
PULSE DURATION. The simplest method of observing pulse width or duration is
that shown in Fig. 13.
Another method is based on the frequency spectrum of a pulse, illustrated in Fig. 15.
(The method of observing the spectrum is to be described below.) The frequency spectrum
of a pulse has a width inversely proportional to the width or duration of the pulse. Fur-
thermore, if the pulse has steep sides, the spectrum has a sharply defined minimum value
at a frequency differing from the maximum by 2/c, as shown in Fig. 15 for a pulse or a
pulsed wave. The frequencies of minimum response can easily be observed by a sharply
tuned receiver. fe having been determined, the pulse duration is 1/2 /c. For example, fc
is 1/2 megacycle for a pulse width
of 1 microsecond, and the minimum
response is displaced 1 megacycle
from the maximuni response.
II, Mi. ..illll, Illllllllllllh illlh. If U is ««"«^* to *"«»« ^
- — — A A - peak and average values of the
0 2fe Frequency /o-2/c-J f0 L-/0 + 2/C power Or voltage or current of a
FIG. 15. Frequency Spectrum of Pulse repeating pulse, the duration may
be computed. The ratio of the
pulse duration to the period of repetition is equal to the ratio of average to peak values,
commonly called the pulse "duty cycle."
AVERAGE VALUES. A repeating pulse has a definite average value of power or
voltage or current. Any one of these average values may be significant in determining the
heating or other accumulative phenomena in a circuit or vacuum tube. For voltage or
current, it is important to specify whether the average or root-mean-square value is to
be measured.
The average power, or the rms value of voltage or current, can be measured by a thermal
instrument with a time constant much greater than the period of repetition of the pulses.
The peak voltage during the pulse is abnormally large for the usual instrument of this
type, and so voltage breakdown may occur, in which event this defect may be corrected
by redesign.
The thermal instruments in common use include the thermocouple, the bolometer
bridge, the lamp with photometer, and the resistor with calorimeter. The most severe
requirements are met in measuring pulsed waves of ultra-high carrier frequencies, say 1000
megacycles and upward.
The bolometer bridge is a d-c four-arm bridge with a temperature-sensitive resistor in
one arm which receives the pulse power to be measured. This device has been improved
by the use of a composition resistor very sensitive to temperature, called the "thermistor."
Since it is desirable for the measuring circuit to present constant resistance, the bridge is
rebalanced by decreasing the d-c level in all arms to restore the variable resistor to the
same temperature, establishing a d-c calibration of the power sensitivity in normal opera-
tion. The device is sensitive to low power of the order of 1 milliwatt and also can be
adapted to greater power.
9-12 PULSE TECENIQTJES
The lamp is useful for medium power of the order of 1 watt. The radiation from the
lamp is indicated by a nearby photocell and meter. It has two great advantages : it requires
no electrical connections between the pulse circuit and the indicating circuit, and it can
be calibrated by direct current. Its one great disadvantage is its large variation of resist-
ance at the high temperatures incidental to radiation of light.
The calorimeter is useful for high power of the order of 1 kilowatt. It can be designed
for nearly constant resistance at very high frequencies, since resistance variation is not
essential in its operation at moderate temperatures.
A possible alternative to the thermal meter is a square-law^ rectifier, which may be
approximated by proper design of a vacuum-tube rectifier. It is important to hold the
peak value within the range of square-law operation, which severely limits the utility of
this type of instrument.
The average value of current or voltage of repeating pulses, assuming zero between
pulses, can be measured in an ordinary magnetic d-c meter having a time constant much
greater than the period of repetition. In a voltmeter, care must be taken that the pulse
voltage is not excessive.
PULSE FREQUENCY. Repeating pulses commonly have a steady value of the pulse
repetition frequency (prf). However, a receiver or a replying transmitter may have a
random pattern of repetition, depending on the traffic, and then it may be desirable to
have a continuous indication of the average pulse frequency over a short period such as
1 sec in order to be aware of overloading.
A constant pulse frequency is easily observed. It is usually an audible frequency and
can be compared with a calibrated audio frequency. The integrating type of frequency
meter which is used for direct-reading audio-frequency meters may be designed for pulse-
frequency measurements. It gives the continuous indication desirable for monitoring a
varying pulse frequency. If the pulse amplitude and width are uniform, the same result
can be obtained by inserting a d-c or average-power meter in the circuit where it will
indicate an average value proportional to the pulse frequency.
PULSE DETAILS. A critical analysis of the details of a repeating pulse or group of
associated pulses may require a display on the oscilloscope with a greatly expanded time
scale. For example, the entire width of the scale may be only a few microseconds, even
though the pulse groups may be separated by a millisecond.
The synchroscope is a special oscilloscope designed for this purpose. Each trace or
sweep is triggered by the first edge of the pulse pattern to be observed, and so close registry
of successive traces is assured, hence the name "synchroscope.'* At the end of each
trace, the spot waits for the signal to start the next trace. Care is taken to insure that each
trace starts at the same point and proceeds at the same rate. Any failure of registry then
indicates variations in the pattern.
FREQUENCY SPECTRUM. A simple pulse or a pulsed wave has a frequency spec-
trum as illustrated in Fig. 15, the former centered on zero frequency and the latter on the
carrier frequency. The significance of the spectrum is the ability to excite a circuit which
selects a bandwidth much less than the width of the spectrum.
The spectrum analyzer is a device for displaying the frequency spectrum on the scope
in the form shown in Fig. 15. As the trace progresses horizontally along the frequency
axis, a narrow-band receiver is tuned over the frequency range. The repeating pulse is
applied to the receiver, and the rectified output is shown by vertical deflection. The pulses
therefore appear as successive vertical lines whose heights show the relative amplitude of
the frequency spectrum. The spectrum is a measure of the frequency bandwidth required
for reproduction of the pulse, as well as the interference that may be caused in adjacent
frequency channels. In the case of a pulsed wave, a symmetrical spectrum indicates pure
amplitude modulation free of frequency modulation.
As appears from the width of the frequency spectrum, a pulsed wave does not give a
sharp indication of resonance in a sharply tuned wavemeter. The carrier frequency is best
defined by the center of a symmetrical spectrum. Therefore it is customary to provide
the analyzer with a very sharply resonant calibrated circuit whose frequency can be
adjusted to put a narrow gap in the center of the spectrum and thereby to determine the
carrier frequency. The calibration of the trap circuit is made on the narrow spectrum of a
continuous wave or long pulses of known carrier frequency.
(For oseiHoscope technique, see Section 11, Wave Analysis, and Section 20, Television.)
FBEQUENCY MULTIPLIERS, DIVIDERS, AND COUNTERS 9-13
PULSE CIRCUITS
By J. J. Okrent
10. FREQUENCY MULTIPLIERS, DIVIDERS, AND COUNTERS
The abrupt changes in amplitude associated with pulse phenomena give rise to a wide-
band frequency spectrum, as indicated above (see Computers, article 7 above; also Section
11, Frequency Measurements). The frequency spectra of certain periodic wave forms, as
rlfuuLrLn_
+B
FIG. 1. Counting Type of Frequency Divider
expressed by Fourier series, are well known. Periodic pulses have strong components of
high-order harmonics. These are produced for frequency comparison by making a stable
sinusoidal oscillator synchronize a relaxation circuit which produces the high-order har-
monics of the stable frequency. The harmonics are compared (by zero beat, for example)
with a signal whose frequency is to be standardized. Substantial output of a harmonic
frequency is obtained by making the relaxation pulse excite a circuit sharply resonant at a
chosen harmonic frequency. Pulse circuits incidentally radiate interfering power at
harmonic frequencies unless they are adequately shielded and filtered.
Frequency division may be accomplished by synchronizing a relaxation oscillator at an
integral submultiple of the synchronizing signal frequency. The natural period of the
relaxation oscillator is made somewhat longer than the interval occupied by the selected
number of synchronizing pulses, and so the pulses expedite the relaxation in each cycle.
Another method of frequency division utilizes a "ring-counter" circuit which counts
the required number of pulses and then generates a trigger pulse and starts counting over
again. In Fig. 1, successive pulses of current /i increase the charge on the capacitor £3
and thereby its voltage E%, for each pulse until the output thyratron conducts, discharging
Cz and producing an output pulse.
-fB
Output
•f Bias
Output
Plate
of B-2
Plate
of B-l
J
J
Plate
of B-0
Input
Input
FIG. 2. Flip-flop Circuits in a Counter
Figure 2 shows flip-flop circuits of a type used in counters and computers. Successive
input pulses, not necessarily at regular intervals, switch successive flip-flops to an indicate
9-14
PULSE TECHNIQUES
ing position. In each flip-flop, either triode, A or B, may conduct; the other triode is then
cut off. Also, if triode A-0 is cut off, triodes A-l and A-2 are conducting. A positive input
pulse will then switch triode .4-0 into conduction, and the coupling between the plate of
B-Q and the grid of B-l will switch triode A-l into conduction. The control grid of triode
.4-1 is thus made sensitive to the next input pulse, and the high plate voltage on B-l may
actuate for that digit an indicating device such as a neon lamp. The coupling between
triodes #-2 and B-0 completes one ring, so that the cycle is repeated every three input
pulses. Output pulses with a frequency one-third that of the input pulses are thereby
obtained.
11. PULSE AMPLIFIERS
The requirements to be met by pulse amplifiers are generally similar to those of television
carrier-frequency and video-frequency amplifiers (see Section 7, Wide-band and I-f Am-
plifiers). The amplifiers must pass the essential frequency components of the signal to
be amplified, with uniform gain and time delay. Any excess bandwidth passes needless
background noise. A compromise choice made in radar systems allows a video bandwidth
(in megacycles per second) equal to the reciprocal of the pulse duration (in microseconds) ,
and double this bandwidth for the modulation sidebands of a pulsed carrier. This is
twice the nominal minimum bandwidth defined on p. 9-11. Some additional carrier-
frequency bandwidth is added for tolerance of detuning from various causes such as
frequency drift.
The amplitude-and-phase spectrum concept (see Section 5, article 13) is useful in specify-
ing low-pass and band-pass amplifiers for pulses and pulse-modulated carrier waves.
Fast recovery of normal operation after overloading by strong signals is required in
systems like radar, in which a weak pulse may immediately follow a strong pulse. Figure
3 shows an i-f amplifier stage having quick recovery. The grid bias returns to normal
VvA, t-B
FIG. 3. Intermediate-frequency Amplifier
immediately after a strong pulse because there is negligible d-c resistance between grid
and ground, and the cathode-circuit time constant is only 0.1 microsecond. The cathode-
circuit time constant is made the minimum consistent with sufficient bias and bypassing.
Plate current is supplied through the damping resistor for the stage. Fast recovery of
normal plate voltage after a strong pulse is relatively unimportant because the operation
of a pentode tube does not depend critically on plate voltage. The inductance L is made
to resonate the distributed capacitance of the wiring and tubes, Cd, without any added
lumped capacitance, in order to obtain maximum stage gain with the required bandwidth.
Video pulse amplifiers are frequently specified in terms of the permissible distortion
of rectangular pulses by the amplifier, rather than by amplitude and phase characteristics.
Thus, it may be required that a specified input pulse after amplification shall have a cer-
tain maximum rise time, fall time, ripple ratio, etc.
Resistance-coupled stages are used for voltage amplification. Because high video fre-
quencies are usually involved, high-transconductance pentodes and relatively small
coupling resistors are used. The product of the coupling resistance by the shunt capaci-
tance places a lower limit on the time of rise and fall "of output pulses. Shunt capacitance
of un-bypassed components and wiring should be made as small as practicable.
In Fig. 4, an input pulse having zero rise time would produce at the f oUowing grid an
amplified pulse having a leading edge rising exponentially with a time constant
n + ^ ("* ohms, microfarads, and microseconds). The amplified pulse would reach 00
per ©eat of peak amplitude in 2.3 times the time constant. The plateau of the pulse
across TI decays exponentially with the time constant fo + r2)Cc, ordinarily much longer
PTJLSE SHAPING CIRCUITS
9-15
than T, the duration of the pulse. If, for example, less than 1 per cent decay is permissible
from this coupling alone, make fa -f r£Cc greater than 100T.
The high-frequency response of resistance-coupled amplifiers may be improved by
compensation and filter techniques discussed elsewhere in this book (see Section 7, Wide-
band Amplifiers, and Section 20, Television) .
When power amplification or impedance change is required, transformer coupling may
be used. High-power pulses are economically obtained from tubes having low average-
power ratings by permitting space current to flow only during pulses. The control grid
+ SC +B +B
Amplifier Cafhode Follower
FIG. 4. Video-frequency Amplifier
in a high-power amplifier is therefore biased negative and driven positive during the
pulses. Transformers may be used to provide the polarity inversion which may be re-
quired in successive high-power stages and also to permit impedance matching. Pulse
transformers will be described below.
Cathode followers (see Fig. 4) are useful in obtaining high-voltage positive pulses across
low impedance such as the coaxial lines commonly used. In successive stages of high-
power pulse amplifiers, cathode followers make transformers unnecessary for polarity
inversion. However, transformers are necessary if voltage amplification is required in
addition to the current amplification obtained in a cathode-follower stage.
12. PULSE SHAPING CIRCUITS
Many of the wave forms used in pulse work are obtained by means of exponentially
changing voltages and currents and by clipping or limiting action in the tubes. In sharp
contrast with linear-amplifier practice, the operating conditions of the tubes in pulse
shaping circuits are so chosen that grid current* may flow or plate current may be cut oft
in order to distort a pulse or to reconstruct a clean pulse.
Clipping or Squaring. In Fig. 5, a sinusoidal voltage is applied to the grid of a tube
through a high resistance. As the grid goes positive, the grid-to-cathode resistance falls
FIG. 5. Squaring a Sine Wave
abruptly, flattening the positive peak of grid voltage. As the grid goes negative, the plate
current is cut off, flattening the negative peak. The output wave form is approximately
square and can be squared further by added stages.
Pulse Narrowing. In Fig. Qa the time constant r\Ci is short as compared with the
duration but not as compared with the time of rise and fall of the applied pulse, e\. The
voltage across r\t from the step at each edge of the pulse, decays exponentially. The pulse
is said to be differentiated, because the voltage across n is approximately proportional to
the derivative of the applied pulse voltage. Either the leading or the trailing edge may be
used by the following stage. If the bias on the tube Tz is large enough to cut off the plate
9-16
PULSE TECHNIQUES
current, only the positive (leading) impulse is amplified. If the bias is zero and r2 is large,
only the negative (trailing) impulse is amplified.
Long pulses may be shortened to a predetermined duration by application through a
high resistance (in Fig. 6b the plate resistance of the pentode) to a delay line which is in
fB Bfas
FIG. 6a. Narrowing a Pulse by R-c Differentiation
parallel with a resistance equal to the characteristic impedance ZQ of the line. The far
end of the line is short-circuited, so that the pulse at the input end of the line is canceled
by a reflected pulse of opposite polarity in twice the one-way delay time, td, of the line.
The undesired pulse of reverse polarity which occurs at the end of the input pulse is
clipped in a succeeding circuit.
2**
utput
Input
FIG. 6£. Narrowing a Pulse by Use of a Delay Line
Another arrangement for obtaining a short pulse of predetermined duration from a
long pulse is shown in Fig. 6c. A half sine wave of short duration is produced in the plate
circuit by the application of a long pulse. The period of the half sine wave is determined
by the inductance of the coil and the distributed capacitance across it. The diode damps the
oscillation on the second half cycle, reducing the oscillation after the first half cycle to a
negligible level.
+ B
FIG. 6c. Narrowing a Pulse by Use of an Oscillatory Circuit
Pnlse Widening, Integration is said to occur in Kg. 7. A positive pulse on the grid
of tube A quickly discharges capacitor Ci, which recharges exponentially with the time
constant rid. Resistance r2 is assumed large as compared with r^ and rsCa large as com-
pared with rid. Tube B is cut off during enough of the exponential discharge to provide
tl*« required pulse duration. The wave forms in solid line are typical of the circuit shown.
IV eoaanectiAg rs to a positive voltage instead of K> ground, a shorter duration and time
ol fall is obtained, as shown by the wave forms in broken line.
RELAXATION CIRCUITS
9-17
+ B
+ B
A— -^-
^2 — connected to + B
instead of to ground
FIG. 7. Widening a Pulse
Clamping or D-c Reinsertion. When it is required that the baseline of a pulse wave
form remain at a fixed voltage in spite of capacitive coupling and changing wave form, the
arrangement shown in Fig. 8 may be used. If the two wave forms shown are coupled by
capacitor C and resistor r\ without the diode, the voltage limits vary as shown because
the average voltage must remain zero. The use of a diode results in a short coupling time
constant for negative voltages, so that the wave extends almost wholly in the positive
direction. The resistance of n is much greater than the resistance of the diode in the eon-
ducting direction (ra). If no grid current flows, the rectifying action of the diode main-
tains on the capacitor a sufficient charge to hold substantially the entire wave positive
,jL47m_
FIG. 8. Baseline Clamping
relative to ground. The diode also permits fast recovery of normal bias if grid current is
drawn by a large positive pulse, because a negative voltage is quickly discharged through
the diode.
13. RELAXATION CIRCUITS
Relaxation circuits are oscillators in which little if any energy is stored from one relaxa-
tion cycle to the next. The circuits have two conditions in which they are at least tem-
porarily stable. When one condition becomes unstable, the oscillator shifts abruptly to
the other condition.
An example of a circuit which has two permanently stable conditions is shown in Fig. 9.
One tube is conducting and the other cut off in each of the stable conditions. Conduction
FIG. 9. Flip-Sop Circuit Stable in Either Condition
is switched back and forth by successive trigger pulses, hence the designation "flip-flop"
circuit. Typical voltages are shown in the figure.
9-18
PULSE TECHNIQUES
In Fig. 10, a capacitor replaces one of the plate-to-grid coupling resistors, and direct
coupling is used between the other plate and grid. Plate current cut off in tube T-2 and
conduction in tube T-3 make a permanently stable condition. A trigger pulse through
tube T-l makes tube T-2 conduct and tube !T-3 be cut off in a temporarily stable condition
T-I
FIG. 10. Triggered Multivibrator
which ends when C discharges sufficiently through r. The circuit then switches back to
the permanently stable condition. The circuit is known as a triggered or one-pulse multi-
vibrator, or a '"univibrator."
The circuit shown in Fig. 11 has only temporarily stable conditions and therefore runs
free. It may be synchronized at the trigger frequency or integral submultiples thereof.
FIG. 11. Free-running Multivibrator
A transformer is used (instead of a second tube) for feedback polarity reversal in the
one-tube blocking oscillator circuit shown in Fig. 12. It is free running unless the C bias
is increased to limit the oscillation to one pulse. A temporarily or permanently stable
condition exists between pulses while the grid capacitor is charged negative beyond
cutoff. The other extreme condition exists during the pulse while the rate of increasing
Output >,
-C
-C •=" ~
FIG. 12. Blocking Oscillator
plate current is limited by the inductance in the plate circuit; this condition causes grid
current to charge the grid capacitor ready for the blocking period. Because plate current
Sows only during the pulses, the blocking oscillator works economically with the low im-
pedances and high currents necessary for short pulses across the inherent capacitance.
ing discharge tubes, such as thyratrons and gas diodes, are used in generating
pulses and sweep voltages by periodic discharge of a capacitor each time the
PULSE TIMING CIRCUITS 9-19
capacitor is charged to the ionizing potential of the discharge tube. The capacitance and
the charging impedance are chosen to give the desired period of pulse repetition.
A number of relaxation circuits particularly adapted for different applications are shown
in other parts of this section,
14. PULSE TIMING CIRCUITS
Various timing problems arise in pulse systems. Pulse repetition rate, duration, and
delay relative to a reference pulse require measurement and control.
Voltage wave forms frequently used for pulse timing are the sinusoidal, the exponential,
and the rectangular. The three wave forms may be compared for basic stability resulting
from their use.
With a sinusoid, if the timing action occurs as the sinusoid passes through the value
zero, the timing is not greatly affected by the amplitude of the sinusoid, and stability of
the same order as that of the inductance and capacitance is obtained.
In commonly used exponential timing circuits, the timing action occurs as the variable
(voltage or current) reaches a predetermined amplitude. The timing is therefore a func-
tion of the initial amplitude as well as the time constant of the exponential change. Sta-
bility of the same order as that of the passive circuit elements requires compensation for
changes in tube characteristics and operating voltages. Stability is generally improved
by using only the early and most rapidly changing part of the exponential wave. Timing
in relaxation oscillators is generally done by exponential changes to predetermined ampli-
tudes.
A rectangular wave sent through a delay line yields a timing wave in which the entire
amplitude change occurs at the most useful time. The stability obtained is limited by
the allowable volume and complexity of the line.
Repetition Rate. A conventional sine-wave oscillator followed by a relaxation or shap-
ing circuit may be used to obtain synchronizing pulses having a stable repetition rate and
short rise time. The sine wave may be converted to a square wave by several clipper
stages as discussed in article 12. The square wave may then be differentiated to obtain a
suitable trigger pulse.
Having a sinusoidal oscillator witk good frequency stability, a phase shifter followed by
shaping circuits may be used to obtain a second pulse with accurately controlled delay
relative to an unshifted trigger pulse. This system has been used in radar equipment to
measure range accurately.
Repetition rate may be determined by a free-running relaxation oscillator such as a
multivibrator, blocking oscillator, or thyratron. The repetition rate is then usually more
subject to drift than if an L-C oscillator is used, but a suitable trigger pulse and a large
range of repetition rates are economically obtained. Figure 13 shows a relaxation oscillator
lutout n
fl
FIG. 13. Repetition Rate Determined by an Exponential Wave Form
providing trigger pulses of fixed duration as the repetition rate is changed. The pulse
duration is determined by the exponential charging of capacitor C through r% and the low
grid-to-cathode resistance of tube T-l. After each pulse the grid of tube T-l is driven
negative for a period determined by the exponential discharging of capacitor C through TI
and the relatively small resistance of r2 and tube T-2. The period between pulses is approx-
imately proportional to the resistance n.
In some applications a delay line may be used to control repetition rate and simultane-
ously supply synchronizing pulses at desired times in each period. Thus, in Fig. 14, the
9-20
PULSE TECHNIQUES
blocking oscillator generates pulses which after traversing the delay line are applied to the
trigger tube and initiate new pulses.
+B abed
; I
_5
Ht
rt 1 5- -._ L.
Delay = £;2 o
ir=
tf_ . !
-c
r — ^-Trigger tube
[locking oscillator
Putse la
-0
* i
td — 4 ^Trigger for pulse 2o
FIG, 14. Repetition Rate Determined by a Rectangular Wave Form
Btiratioiu Pulses having a required duration may be generated by relaxation circuits
or by pulse-forming lines and thyratrons, as discussed in article 15, "Pulse Modulation
of an Oscillator." Alternatively, sinusoidal or other wave forms may be passed through
pulse shaping circuits (see above) to produce pulses of the required duration.
4-B
Output
Toward + B
~LT
Sync.
FIG. 15. Poise Duration Determined by an Exponential Wave Form
A cathode-coupled one-pulse relaxation circuit is shown in Fig. 15 to illustrate control
of pulse duration by exponential voltage change.
Blocking oscillators deliver maximum power during the pulse and therefore are adapted
for high-power pulse equipment. Nominal control of pulse duration is obtained by means
-fB
-c •=•
False Diu-atkm Determined by a Rectangular Wave Form
of grid capacitors and con-
trol of transformer induct-
ance, in the circuit of Fig,
12. Precise duration and
better pulse shape are ob-
tained by means of a delay
line as in Fig. 16. The
transformer inductance is
made large; the feedback,
the line impedance, and
the line terminating resist^
ance are so chosen that
the oscillator is shut off
when the wave of grid
PULSE MODULATION OF AN OSCILLATOR
9-21
current reflected from the open end of the line reaches the terminating resistor. The
pulse duration is then determined mainly by the round trip delay of the line and is little
affected by variations in other circuit elements.
Delay. A complex wave may be delayed by passage through a delay line while main-
taining substantially the same wave form. If it is only required that a delayed pulse be
produced, the initiating pulse may trigger a relaxation oscillator, and the trailing edge of
the relaxation pulse may be used after differentiation as the delayed pulse. The delay
of the trailing edge of the relaxation pulse may be varied in accordance with a desired
Delay line, td, ZQ
+B
(a) Delay Line
ir
Sync.
(6) Relaxation Oscillator (Optional Pulse-time Modulation)
H-B
(c) Resonant Circuit
FIG. 17. Circuits for Delaying Pulses
modulation for obtaining pulse-time modulation in a communication system. Special
cathode-ray tubes have been developed to facilitate time modulation of the many time-
sharing pulse channels in pulse-time multiplex systems. In another method, a resonant
circuit is keyed on or suddenly shocked, and a delayed pulse is produced after a fraction
of a cycle of oscillation. Typical circuits using (a) "the delay line, (6) the relaxation oscil-
lator, and (c) the resonant circuit are shown in Fig. 17.
The delay line can accept pulses having random spacing such as might be encountered
in the output of a receiver. The other circuits illustrated must pass through a complete
delay and recovery cycle between pulses and therefore are best used with isolated pulses.
15. PULSE MODULATION OF AN OSCILLATOR
An oscillator may be made to operate in pulses by including in its grid circuit a capacitor
which charges during the oscillation and blocks or stops the oscillation. This is one form
of the blocking oscillator. Oscillations start again after the capacitor has discharged suffi.-
9-22
PULSE TECHNIQUES
Output
Bias
FIG. 18. Pulse-modulated Carrier-frequency Oscillator
ciently. The pulse recurrence rate and the pulse duration are approximately controlled
by the time constants in the circuit, but only with limited stability.
The recurrence rate of a blocking oscillator may be stabilized by the use of synchronizing
circuits to start tube conduction sooner after each pulse than would otherwise happen.
The pulse duration may
be stabilized by making
a time-delay network
shut off the oscillator.
The oscillator in Fig.
18 has provision for syn-
chronization by a posi-
tive pulse applied to the
grid. A delay line in the
cathode circuit shuts off
the oscillator after a
time interval of twice
the line delay. The dis-
charging resistor r is
usually many times as
large as Z^ the wave
impedance- of the line.
At the start of the pulse
the cathode current flows through an impedance approximately equal to Z0, and develops
a voltage wave B which travels through the line. The wave is reflected with the same
polarity by the open far end and returns to increase the voltage at the cathode to approxi-
mately twice the initial voltage, stopping the oscillator.
Pulse modulation may also be accomplished by grid or plate modulation of an oscillator
or amplifier. If high power is required, plate modulation of an oscillator is generally most
economical. With plate
modulation, the high volt-
age is impressed] on the os-
cillator tube only during the
pulses. The design of the
oscillator tube is thereby
made easier, or conversely
the permissible maximum
plate voltage on a given
tube design may be in- Driver
creased far beyond the
direct- voltage rating.
A vacuum-tube modulator is shown in Fig. 19. The modulator tube, cut off between
pulses, is driven hard so that it passes high current through low impedance during the
pulses. The modulator acts as a switch connecting the load to the B supply only during
the pulses.
A thyratron pulse modulator is shown in Fig. 20. The artificial line is charged through a
high resistance rc between pulses. By the use of the line instead of a single capacitor, a
-fB -C
Modulator
FIG. 19. Vacuum-tube Modulator
- oj^iTY/iry^j^^YyT^o
!'
4-B
Sync,
— C
FIG. 20. Thyratron Modulator
rectangular pulse may be obtained rather than an exponentially decaying pulse. The
thyratron discharges the line into the load and must deionize before the line can recharge.
3>eionization is expedited by making the thyratron resistance plus the transformed load
rcsisliuace somewhat less than the line impedance so that the thyratron plate is driven
sligfetJty negative just after the pulse.
MODULATING THE CHARACTERISTICS OF PULSES 9-23
For high-voltage applications, the preferred form of artificial line is the "Guillemin
line," shown in Fig. 29 (e) below. Also, the thyratron may be replaced by a spark gap.
Higher efficiency and faster charging of the line may be obtained by replacing the charging
resistor rc by an inductor. The line is then charged in a half-cycle of a charging oscillation,
between pulses, to approximately twice the power supply voltage. A diode may be con-
nected in series with the inductor to prevent discharge back into the power supply.
Pulse modulation imposes on an oscillator severe requirements of fast starting and stop-
ping. The oscillator must ordinarily start from the background noise in the circuit and
build up to maximum amplitude in a time interval which is much shorter than the pulse
duration. Random variations in the noise amplitude cause random variations in starting
time, termed "jitter."
To explain the starting and stopping time, the essential elements of the oscillator are
indicated in Fig. 21. They are the resonator CL and the conductance g. During the
starting time of a pulse, the net conductance is made nega-
tive by feedback; during the stopping time it is positive as
determined by the damping of the circuit augmented by
its useful load.
The starting or stopping time constant of oscillations is
2C/g The starting time, for the oscillations to build up
by regeneration from the noise level, is of the order of 20
times the time constant determined by the negative con-
ductance, and the jitter is somewhat less than this time
constant. The stopping time is about equal to the stopping time constant, since the oscil-
I
T
Equivalent Circuit of an
Oscillator
lation is merely damped from its peak value after the regeneration is cut off.
are shown in Fig. 8, p. 9-06.
These effects
16. MODULATING THE CHARACTERISTICS OF PULSES
Preceding sections of this chapter have indicated ways of forming pulses and controlling
their characteristics. Coding of pulses for identification of the source or for transmission
of information may be accomplished by mechanical switching or by electronic switching
or modulation. Pulse duration may be changed by connecting or disconnecting sections
in a delay line used to control a blocking oscillator. Similarly, the constants of a shaping
circuit or relaxation circuit may be switched.
The circuit shown in Fig. 17(6) permits electronic modulation of pulse width such as
might be used in a communication system. Differentiation of the output pulse, as shown
in the figure, yields a pulse having electronically modulated phase relative to a base or
marker pulse. Pulse phase or time may also be modulated at an audio rate by addition
of audio voltage to linear sawtooth timing pulses as shown in Fig. 22. No plate current
• Delay of modulated pulse
FIG. 22. Pulse-time Modulator
flows until the sum of the audio, the sawtooth, and the bias voltages exceeds the cutoff
voltage of the mixer tube. The timing of the leading edge of the resulting plate-current
pulse varies in direct proportion to the instantaneous value of the audio voltage. The mixer
9-24
PULSE TECHNIQUES
output pulse may be differentiated and shaped to obtain the desired wave form for pulse
modulation of a carrier wave.
A group of pulses may be obtained by shaping a sine wave which has the proper perio-
dicity, to obtain trigger pulses for a relaxation circuit. The sine wave is initiated and
ended by a gate pulse long enough to permit generation of the required number of pulses.
Figure 23 shows one such arrangement. Triode A is conducting normally. A negative
FIG. 23. Multiple-pulse Generator
gate pulse cuts off the triode, developing a positive gate and a free oscillation to drive the
grid of the pentode J?. At the end of the gate pulse the oscillations are quiokly damped
by the plate resistance of the triode. The number of pulses may be changed by switching
the gate pulse duration.
Figure 24 shows the elements of a two-pulse generator using a delay line. A modification
of this arrangement in which the pulse spacing would correspond to altitude has been
proposed for use in air navigation (Lanac). An initiating pulse passes through a delay
ri
FIG. 24. Double-pulse Generator
line and is absorbed by the resistor terminating the line. The line is tapped to permit
application of the pulse, after the required delay, to the grid of a tube. The direct and
delayed pulses are mixed to produce a pair of pulses with variable spacing.
17. PULSE DETECTORS
Pulses are distinguished from sinusoidal and steady waves by rapid changes in ampli-
tude, large ratio of peak to average value, small duty cycle, and wide frequency spectrum.
Tfee detection of pulses requires detecting means responsive to the special characteristics
®l praises, tsaaially to t&mr tisae boundaries as distinguished from their peak amplitudes.
Bandwidth requirements have been discussed earlier in this section. Pulse amplifiers
»ay isielml© Sites or coupling systems which favor pulses having certain characteristics,
9-26
PULSE TECHNIQUES
require more pulses in a group. The timing of two or more pulses in a group may be used
for altitude coding in an air navigation system (Lanac) as mentioned previously.
Phase or time modulation of pulses in a communication system may be converted to
audio signals by a corresponding type of detection. Phase modulation may be detected by
providing reference pulses
of uniform periodicity and
using these to form gate
pulses of suitable phase
which the phase-modulated
pulses overlap more or less
in accordance with the mod-
ulation. If the gate and
the phase-modulated pulses
are applied to a coincidence
mixer, plate current will
flow during the interval of
pulse overlap. The plate
current, averaged over a
few pulses, is then modu-
lated in accordance with
the phase modulation of
the pulses. Special beam-
deflection tubes have been
Delayed-
Mixer output-^ | [
FIG. 27. Double-pulse Decoder
developed for phase modulation and synchronous detection of many time-sharing channels
in & pulsed multiplex system.
18. VACUUM TUBES
Most vacuum tubes, at the date of writing, have not been rated for pulse applications
(see Section 4, especially pulse tubes such as magnetrons and thyratrons). However,
many vacuum tubes have been used in pulse applications after rough estimation of their
pulse capabilities from their ordinary ratings. The principal factors are peak and average
cathode current, peak and average electrode voltages, electrode power dissipations, and
tube life.
If a tube has class C amplifier ratings, the cathode current for long pulses may safely
be 4 or 5 times the class C average-current rating. The average current should not exceed
the class C average-current rating. For pulses a few microseconds in duration, peak cur-
rents of about 50 times the class C average-current rating may be taken from oxide-coated
cathodes, with tube life commonly exceeding 500 hours. Pulse current densities of 10 to
20 amp per sq cm are used with specially processed oxide-coated cathodes. The cathodes
must be heated to their operating temperature before large currents are permitted.
The ordinary peak-voltage ratings of tubes may often be safely exceeded in pulse appli-
cations. Insulation breakdown inside the tube, electrolysis of the glass, or poor plate-
current cutoff characteristics may fix the permissible peak voltage. The peak plate voltage
in class C applications is about twice the average plate voltage; this is usually a justifica-
tion for permitting pulse peak voltages twice the rated average plate voltage. If the plate
voltage is applied only during pulses, the sparkover voltage may set the limit at a much
higher voltage.
Beam power tubes in pulse modulators are operated at high screen voltage in order to
reduce the driving power required. The plate voltage is usually low during pulses of
current flow, so that average plate power dissipation is low. Screen dissipation is high,
however, and often limits average power. Permissible limits of plate and screen dissipa-
tion may be reduced as peak-voltage ratings are increased.
The space-charge effects which suppress secondary emission from the plate in beam
tubes also tend to limit the flow of pulse current at low plate voltage. The usually desired
properties of beam tubes are even more important for pulse amplifiers of very high power
used as modulators. Secondary emission from the control grid is minimized to avoid loss
of control caused by reverse grid current and to prevent parasitic oscillation.
A number of thyratrons specifically intended for pulse modulation are available. Minia-
ture types deliver pulses of peak power of kilowatts; larger types deliver megawatts. Fast
dekmization is obtained in tubes filled with the lighter gases such as hydrogen and helium,
slower deionization with argon and xenon. Cathode current densities are of the same order
as m higfe-vactium tubes but with much less voltage drop between plate and cathode. The
internal voltage drop is high at the start of ionization, very rapidly decreasing as ionization
rme&es saturation. A maximum rate of rise of current is specified to limit the plate dissi-
PULSE TRANSFORMERS
9-27
pation and the ion bombardment of the cathode at the start of the pulse. The rate of rise
of current is usually limited by some inductance in series with the plate of the thyratron.
It is worthy of mention that, at the high currents used in pulse work, the transconduct-
ance of vacuum tubes is greater than usual, and transit time is reduced by the correspond-
ing high voltages. The performance of a tube in a pulsed oscillator is therefore often better
than its continuous-wave performance at high carrier frequencies subject to transit-time
effects. In fact, some types will oscillate efficiently in high-power pulses at frequencies
so high that continuous oscillation is impossible at their Tnq.xJTn \iirt d-c ratings.
19. PULSE TRANSFORMERS
The problem of designing a pulse transformer is generally similar to that of designing
an audio-frequency transformer but for higher-frequency components with corresponding
-f-B -C
(a) Interstage Transformer
(6) Equivalent Circuit of 1:1 Transformer
Rise and ripple of
due to Lj, Clt C2, C3
Decay of £2
due to Tlt T2, \-
Backswlng of £2
duetoLm; rlt
Ci, C2 * A-T^and r2 large
(c) Pulse Transformer Wave Forms
FIG. 28. Pulse Transformers
reduction in size. Maximum mutual inductance, minimum leakage inductance, and min-
imum incidental capacitance are desired. The ratio of maximum to minimum essential
frequency components involved in faithfully transforming a single pulse wave form may
be 100 to 1. If the pulse duration may vary by 10 to 1> the frequency ratio may be 1000
to 1. The requirements for high-power modulator transformers are usually much less
severe in frequency ratio.
A rough estimate of transformer specifications may be obtained by analysis of the
circuit of Fig. 28 (a) and the equivalent circuit shown in Fig. 28(6). A turns ratio of 1 to
1 is assumed. The mutual inductance Lm may be neglected in estimating the rise time
0-28 PULSE TECHNIQUES
of the pulse. If n and Ci are small, the rise time is roughly VLiCz or Li/rz, whichever is
greater. The magnetizing current at the end of the pulse is
if the pulse duration is T* The decrease in voltage during the pulse and the backswing
at the trailing edge, both of which are caused by the magnetizing current, are roughly in
the ratio
Affa_ T nr2 (2)
Et = Lm TI 4- rz
if ri and rz are small and linear. If n and r3 become large on reversal of polarity, the back-
swing is determined by Im, Lm, Ci -f £2, Cs, and rm. rm represents the apparent shunt
resistance of eddy currents and hysteresis in the core loss.
To reduce eddy currents or skin effect in the core, very thin laminations are used for
pulse transformers. Permalloy and silicon-steel tapes from 0.0001 to 0.003 in. in thickness
are wound into toroidal cores which are sliced for assembly with coils. Reduction of skirt
effect in the core permits greater ratios of mutual to leakage inductance by increasing the
depth of penetration and the resulting effective permeability of the core volume. The
available flux swing in the core may sometimes be increased by the use of reverse-
magnetizing direct current. Because pulse wave forms are usually unidirectional, and the
core has some retentivity, saturation may otherwise occur with a small flux swing, per
pulse. Some core materials especially suited for pulse applications are listed below.
Because of restrictions on leakage inductance, high-voltage pulse transformers are
difficult to insulate. Impregnation with oil or polymerized resins to eliminate air spaces
and moisture are effective in preventing corOna and raising the breakdown voltage.
Table 1. Core Materials for Pulse Applications
Name and Manufacturer Description
Hypersil Wound silicon-steel tape: grain-oriented 0.002 in1
Wesiinghouse Electric Corp. thick tape for high quality; plain 0.003 in.
tape for less critical application.
Permalloy Wound permalloy tape: from 0.0001 to 0.002 in.
Bell Telephone Laboratories thick; several different alloys.
Silicon NicaJloy Conventional laminations: type B9W4A. *
General Electric Co.
Sinimax and Monomax Conventional laminations: several different
Allegheny Ludlum Steel Corp. alloys (permalloys).
20. DELAY LINES *
A delay line is a network used for storing the energy of a pulse pattern and delivering
out the same energy at a later time. (See Section 5; Networks, Lines, Transients.) The
simplest form is a transmission line, in which case the delay is determined by the distance
along the line at a velocity somewhat less than the velocity of light. While the transmission
line or wave guide may give the best performance, it requires a length too great for most
purposes, so more concentrated forms have been devised to save space.
Delay lines are used for two general purposes: one is the relative timing of different
operations; the other is the delayed reproduction of a pulse pattern. The former may be
tolerant of distortion in the delay process and can even be accomplished by other kinds
of timing circuits such as relaxation oscillators. The delayed reproduction of a pulse
pattern, however, places the most severe requirements on a delay network, especially
against amplitude and phase distortion. For either purpose, precision of timing may be a
requisite which involves directly the stability of the network and indirectly the fidelity of
reproduction and the stability of associated circuits.
Figure 29 shows some typical concentrated delay networks. They rely on coils for
concentrating the inductance and on dielectric for concentrating the capacitance. Further
concentration of inductance may be obtained by iron-dust cores for the coils. *
The continuous coil with capacitive loading is shown in Fig. 29 (a). In a typical form, a
coH of fine enameled wire is wound on a flexible core of insulation material having such
small diameter that it can be coiled. The winding is wrapped with thin dielectric tape for
eapadtive loading, and the other conductor is provided by a braided sheath of fine
* Tfefe article by Harold A. Wheeler.
DELAY LINES
9-29
enameled wire. The sheath acts as a capacitive shield but not as an inductive shield,
because the latter would destroy the desired inductance of the coiled inner conductor.
The entire line is protected by a covering of insulation.
In a continuous coil, the mutual inductance along its length has the effect of decreasing
the effective inductance at higher frequencies relative to that of lower frequencies, which
causes phase distortion. In Fig. 30, the
curved dotted line (a) shows this effect.
Uniform delay, free of distortion, requires
a straight phase curve illustrated by the
solid line (&). It has been found possible
to approximate this ideal by introducing
substantial distributed capacitance in
parallel with the series inductance, as is
also shown in Fig. 29 (a). This causes
the effective inductance to increase with
frequency and can be designed to com-
pensate for the opposite effect of mutual
inductance along the coil. Without such
-TTTT T.
Ll
r Total
°J
Continuous Coif
Total
(6) Continuous Bifilar Coil
c/TTv^WrvTT^
- T T T T . C
Lumped Line
oil oU
_Z2 .Z2
(<i) Open-circuit Reflecting Line by
Parallel Components
6/! 4f, 2f,
r^S r^S r^S
HL,JLiJLJlh
ire; 'ic lie c
2 T 2"
o 1
Frequency
FIG. 30. Phase Distortion of Continuous Coil
compensation, the effect may be reduced
by using a coil diameter very small as
compared with its length, which tends,
however, to defeat the aim of concentra-
tion.
The low-frequency delay (initial phase
slope) of a delay line is
•• VOL
(3)
in terms of the total shunt capacitance C
and total series inductance L (including
mutual inductance) . The corresponding
wave impedance (characteristic imped-
ance or image impedance) is
ZQ
(4)
| Open-circuit Reflecting Line by
Series Components
Any of the following sets of units may
be specified, the last (long used by Dr.
Alan Hazeltine) being generally most convenient:
FIG. 29. Delay Lines
T
C
L
seconds
farads
henrys
ohms
ohms
mh
kilohms
As an example, a rather long coiled line of 1 mjuf and 1 mh has a delay of 1 /is and a wave
impedance of 1 kilohm.
Another form of coiled line, shown in Fig. 29(6), is made of two coils wound in opposite
screw-^direotions on the same core. One coil is wound in one direction on the core, then
the other is wound on top in the opposite direction. The insulation may be only the
enamel on the wires, or it may also include some thin layers of dielectric. This method
gives the inductance of a two-layer coil with convenient capacitive loading. It is useful
as a balanced four-terminal circuit or as a two-terminal reflecting line with far end on open
circuit or short circuit.
The low-pass filter of Fig. 29 (c) is a lumped delay line. Its useful bandwidth is some-
what less than its cutoff frequency and decreases further with more sections. The con-
9-30
PULSE TECHNIQUES
stant-fe type (without mutual inductance) has concave phase distortion as shown in Pig.
31 (a). By converting to an m-derived type, by the addition of mutual inductance M
between adjacent inductors, it is possible to approach the ideal linear phase (5) to the
- approximation indicated by curve (c). For a line of many
sections, the optimum value of the design parameter m is
V3/2 = 1.22. The number of sections required is
N = -fJT
m
(5)
0 Frequency fa
FIG. 31. Phase Distortion of
Lumped Line
in terms of the cutoff frequency Je (Me) and the delay T (jus).
As an example, a pulse 1 fts wide can be delayed 2 jus by a
network of fe = I Me and N « 5 sections.
In a concentrated delay line with phase correction, espe-
cially if the delay is many times the permissible widening of the
pulse, the attenuation increasing with frequency is likely to
impose the practical limitation on the useful bandwidth. Therefore all losses must be
minimized to secure the optimum design in limited space.
A reflecting line is often useful and has the advantage of a round trip which doubles the
delay. The voltage polarity of reflection is direct or reverse, depending on whether the
far end of the line is an open or short circuit. Ordinarily the near end is terminated with a
resistance load matching the line impedance to preclude multiple reflection.
A reflecting line becomes a two-terminal network whose essential properties are expressed
by the variation of impedance with fre-
quency. An ideal delay line of uniform
delay and no losses has a pure react-
ance as shown in Fig. 32 if the far end
is on open circuit. The alternate zeros
and poles are at odd and even multiples
of the fundamental frequency:
(6) -
At this frequency, the length is 1/4 FIG. 32. Impedance of Open-circuit Reflecting Line
wavelength in the line.
The impedance of a reflecting line can be duplicated over a limited frequency bandwidth
by other two-terminal impedance networks which sometimes have advantages. Figure
29 (d) presents the reactance pattern of Fig. 32 by a parallel connection of several series-
tuned circuits having equal values of inductance but
such values of capacitance as to resonate at odd
multiples of the fundamental frequency. Figure
29 (e) presents the same reactance pattern by a series
connection of parallel-resonant circuits having equal
values of capacitance and resonated at even multi-
ples. This last network has a great advantage in
pulse discharging functions (as proposed by E. A.
Guillemin) because only the isolated capacitor C has
to take the high-voltage charge preparatory to the
discharge; the other capacitors can have much lower
voltage ratings.
When a charged delay line is discharged into a
matched load, the output is a pulse whose width is (&) Concave Phase Curvature (Fig. 31)
the round-trip delay 2TT as shown in Fig. 33. The
pulse starts suddenly by the discharge of energy
R
—Time
(Or) Convex Phase Curvature (Fig, 30)
-Time
2T
-Time
(c) Phase Correction
FIG. 33. Pulse Discharge of a TJ"e into a
Matched Load
FIG. 34. Delay of a Pulse by a Reflecting
Line on Open Circuit, Showing the Effects
of Distortion
near the terminals, but the trailing edge is sloping because the delayed energy is subiect
to *b© distortion in the line.
Time
BIBLIOGRAPHY 9-31
Figure 34 shows the distortion of a pulse subjected to round-trip delay in a reflecting
line on open circuit. In every case the pulse is decreased in area by the attenuation and
is widened by the amplitude distortion limiting the frequency bandwidth. The effects
of phase distortion can be estimated by the method of paired echoes. The leading tran-
sient (a) and the trailing transient (6) are charac-
teristic of convex and concave phase curvature,
shown in Figs. 30 and 31. The former occurs in con-
tinuous coiled lines and the latter in lumped lines. In
either case, phase correction (Fig. 34c) removes the
transient oscillation, since the oscillation is caused _
bv subnormal or abnormal delay of the higher- -n^ oe T\ i JT> •, * -n ,
u<y , r • XT. i Fis* 35- Delay and Reversal of a Pulse
frequency components of energy in the pulse. by a Reflecting Line on Short Circuit
If the direct and reflected pulses have to be
separated, a delay line on short circuit (or an equivalent two-terminal network) is used to
secure the result shown in Fig. 35. Since the respective pulses are of opposite polarity,
one or the other can be selected by a rectifier.
BIBLIOGRAPHY-
Note. Under each heading, the references are listed chronologically (except for the *TB" items,
whose dates of publication do not appear in their titles). The "PB" items are issued by Office of
Technical Services, U. S. Department of Commerce, Washington 25, D. C.
Asterisks (*) denote some of the principal references or further bibliographies on each subject.
Radar
* 1. Navy Dept., Radar System Fundamentals, Navships 900,017 April 1944.
* 2. Navy Dept., Radar Electronic Fundamentals, Navships 900,016, June 1944.
3. D. G. Fink, The Radar Equation, Electronics, Vol. IS, No. 4, 92-94 (April 1945).
4. W. E. Moulic, Operational Elements of a Radar System, Electronic Industries, Vol. 4, No. 5,
76-80, 225, 226 (May 1945).
5. Jordan McQuay, Practical Radar, Radio News: Part I, Vol. 33, No. 6, 29 (June 1945);
Part 2, Vol. 34, No. 1, 38 (July 1945) ; Part 3, VoL 34, No. 2, 39 (August 1945) ; Part 4,
Vol. 34, No. 3, 40 (September 1945); Part 5, Vol. 34, No. 4, 44 (October 1945).
* 6. R. B. Colton, Radar in the United States Army, Proc. I.R.E., VoL 33, 740-753 (November 1945).
7. Report on Wartime Electronic Developments, Electronics, Vol. 18, No. 11, 92-93 (November
1945).
*8. Radar Specifications, Electronics, Vol. 18, No. 11, 116-119 (November 1945).
* 9. The SCR-584 Radar, Electronics: Part I, VoL 18, No. 11, 104-109 (November 1945) ; Part II,
Vol. 18, No. 12, 104-109 (December 1945).
10. C. W. Watson, Ground-controlled Approach for Aircraft, Electronics, Vol. 18, No. 11, 112-115
(November 1945).
11. H. A. Straus, L. J. Rueger, C. A. Wert, S. J. Reisman, M. Taylor, R. J. Davis, and J. H.
Taylor, The MPG-1 Radar, Wectronics: Part I, Vol. 18, No. 12, 92-97 (December 1945);
Part II, Vol. 19, No. 11, 110-117 (January 1946).
12. W. C. Hendricks, Lightweight Radar for Early Warning, Communications, Vol. 26, 54 (January
1946).
* 13. W. C. Tinus and W. H. C. Higgins, Early Fire-control Radars for Naval Vessels, Bell Sys.
Tech. J.t VoL 25, 1-47 (January 1946).
* 14. H. A. Zahl and J. W. Marchetti, Radar on 50 Centimeters, Electronics, VoL 19: Part 1, No. 1,
98-104 (January 1946); Part 2, No. 2, 98-103 (February 1946).
15. W. T. Spicer, The GCA Landing System, Bendix Radio Engineer, January 1946. (Radar on
3000 Me or 10,000 Me with PPI display.)
16. H. V. Hermansen, Bendix Radio Engineer, January 1946.
17. A Tool for Traffic Control — Telerad, Air Transport, VoL 4 /No. 1, 73-78 (January 1946)
18. I. F. Byrnes, Merchant Marine Radar, fl.C.A. Rev., VoL 7, 54-66 (March 1946).
19. Jack Mofenson, Radar Echoes from the Moon, Electronics, Vol. 19, No. 4, 92-98 (April 1946).
* 20. D. A. Quarles, Radar Systems Considerations, Elec. Eng., Vol. 65, Trans., pp. 209-215 (April
1946).
* 21. G. V. Holdam, S. McGrath, and A. D. Cole, Radar for Blind Bombing, Electronics, VoL 19:
Part I, No. 5, 138-143 (May 1946) ; Part II, No. 6, 142-149 (June 1946).
* 22. O. P. Ferrell, London Radiolocation Convention, Radio, Vol. 30, No. 5, 26, 28,47, 48 (May 1946).
23. L. N. Ridenour, Radar in War and Peace, Elec. Eng., VoL 65, 202-207 (May 1946).
24. R. C. Jensen and R. A. Arnett, Air-borne Radar for Navigation and Obstacle Detection, Elec.
Eng., VoL 65, No. 5, 307-313 (May 1946).
25. H. Busignies, P. R. Adams, and R. I. Colin, Aerial Navigation and Traffic Control with
Navaglobe, Navar, Navaglide and Navascreen, Elec. Communication, VoL 23, No. 2, 113—
143 (June 1946).
26. E. I. Green, H. J. Fisher, and J. G. Ferguson, Techniques and Facilities for Microwave Radar
Testing, Bell Sys. Tech. J., VoL 25, No. 3, 435-482 (July 1946). *<>•
27. Thomas Grover and E. C. Kluender, The Electronic Navigator, Communications, VoL 26, No. 8,
30, 36-39 (August 1946).
* 28. E. G. Schneider, Radar, Proc. I.R.E., Vol. 34, 52&-57S (August 1946).
29. L. R. Quarles and W. M. Breazeale, Factors Affecting the Range of Radar Sets, Elec. Eng.,
VoL 65, Trans., pp. 546-548 (August-September 1946).
* 30. L. V, Berkner, Naval Airborne Radar, Proc. I.R.E., VoL 34, 671-706 (September 1946).
31. E. D. Hart, Navigational Rads-r in Merchant Ships, Electronic Eng., VoL 18, 265-267 (September
1946).
32. J. H. Cook, Airborne Search Radar, Bell Lab. Rec., VoL 24, 321-325 (September 1946).
9-32 PULSE TECHNIQUES
33. M. L. Lawrence, A 100-kw Portable Radar Transmitter, Communications, September 1946,
34. C.PB.*Barnel Radar Carrier-based Planes, Electronics, Vol. 19, No. 10, 100-105 (October 1946).
35 H B Brooks Weather Forecasting, Electronics, Vol. 19, No. 10, 84-87 (October 1946).
36. M.I.T. Radar School Staff, Principle* of Radar, 2nd Ed. McGraw-Hill (1946).
37 L. H. Lynn and O. H. Winn, "Marine Radar for Peacetime Use," Elec. Eng.t Transactions,
Vol. 65, 271 (May 1946). <
38. PB1SQ42, Navy Dept., Radar SU-1 with PPI display.
39. PB 19248, War Dept., Radar APS-4A on 9400 Me.
40. PB20810, Navy Dept., Radar APS-4.
41. PB20S12, War Dept., Radar APS-15 training course.
42. PB20S13, Navy Dept., Radar APS-3, on 9400 Me.
43. PB2240Q, Navy Dept., Radar CXAM-1 on 195 Me.
44. PB23435, War Dept., Radar TPS-3.
45. PB23438, War Dept., Radar SCR-6S2-A.
46. PB23447, War Dept., Radar SCR-682-A.
47. PB24913, Navy Dept., Radar SOS.
48. PB24933, Navy Dept., Radar SR with A-type and PPI displays.
49. PB24936, Navy Dept., Radar SJ-1 with PPI display.
50. PB24938, Navy Dept., Radar SA-3 on 200 Mo.
Radio Pulse Altimeters
61. Heinrich Lowry, Electric Proof and Measuring of the Distance of Electrically Conductive
Bodies, U. S." Pat. 1,585,591, July 17, 1923-May 18, 1926.
62. Gregory Breit and M. A. Tuve, A Test of the Existence of the Conducting Layer, Phys. Rev.,
Vol. 28, 554-575 (September 1926).
63. R. W. Hart, Measuring Distance, U. S. Pat. 1,924,156, May 19, 1930-Aug. 29, 1933.
64. Ezekiel Wolf, Measuring Distance, U. S. Pat. 1,924,174, May 19, 1930-Aug. 29, 1933.
65. D. L. Plaistowe, Radio Apparatus for Detecting Aircraft, U. S. Pat. 2,207,267, July 11, 1938-
July 9, 1940.
66. Joseph Lyman, Radio Absolute Altimeter, U. S. Pat. 2,227,598, July 3, 1937- Jan. 7, 1941.
* 67. Albert Goldman, Pulse-type Radio Altimeter, Electronics, Vol. 19, No. 6, 116-119 (June 1946).
68. P. G. Suizer, Ionosphere Measuring Equipment, Electronic*, Vol. 19, No. 7, 137-141 (July 1946).
Navigation and Identification by Poises
* 71. Editor (D. G. Fink), The Loran System, Part I, Electronics, Vol. 18, No. 11, 94-99 (November
1945). Loran Receiver-indicator, Vol. 18, No. 12, 110-115 (December 1945). Loran
Transmitting Stations, Vol. 19, No. 3, 109-115 (March 1946).
72. Editor, Fundamentals of Radar — Pulse Methods Applied to Navigation, Wireless World,
VoL 52, 23-26 (January 1946).
73. Editor, Fundamentals of Radar. 5. Beacons Employing Pulse Technique, Wireless World,
VoL 52, 55-56 (February 1946).
74. D. Davidson, Loran Indicator Circuit Operation, Elec. Ind., Vol. 5, No. 3, 84-93, 126, 128,
130, 132 (March 1946).
* 75. S. W. Seeley, Shoran Precision Radar, Elec. Eng., Vol. 65, Trans., pp. 232-240 (April 1946).
* 76. J. A. Pierce, An Introduction to Loran, Proc. I.R.E., Vol. 34, 216-234 (May 1946).
*77. Hazeltine Electronics Corp., Lanac Air and Marine Navigation (1946).
78. PB20811, War. Dept., Radar Transponder Beacon APN-7 on 3300 Me.
79. PB23325, P. J. Herbet, Ultra Portable Racon,
*80. PB23434, War. Dept., Radar RC-145-A.
81. PB23448, War Dept., Radar RC-150B, RC-151, etc.
82. PB24920T Navy Dept., Radar CPN-3.
83. PB24922, Navy Dept., Radar BQ.
} Sonar
* 91. R. J. Evans, Echo Ranging Sonar, Electronics, VoL 19, No. 8> 88-93 (August 1946)
* 92. G. B. Shaw, Echo Depth Sounder for Shallow Water, Electronics, VoL 19, No. 9, 88-92 (S*r>tem,
ber 1946).
93. Thomas Roddam, Radar in Nature, Wireless World, VoL 52, 286-288 (September 1946)
©4. PB19955, Navy Dept., Sonar QBE, ABE, etc,
95. PB25497, O. R. Smith, Fish Schools— Location by Sonic Equipment.
Pulse Techniques and Measurements
* 101. D. G. Fink, ilfieriwcwe Radar, Vol. 1, Theory and Practice of Pulsed Circuits (July 1942).
* 102. J. G. Brainerd, Ultra-high-frequency Techniques. Van Nostrand (1942). Chapter 4 triggei
circuits, pulse-sharpening circuits and oscillators, pp. 168-207.
* 103. Navy Dept., Microwave Techniques, Navships 900028 (June 1944).
104. Aflfm Easton, Puke Response of Diode Voltmeters, Electronics, VoL 19, No. 1, 146-149 (Jan-
uary 1946).
106. Allan Easton, Measuring Pufee Cteacteristies, Electronics, Vol. 19, No. 2, 150-154 (February
* 106' G "0^ at Frequeno ies
* 107- '• *1'- iad FacUities for Microwave ^
* 108, M.I.T, Radar School Staff, Principles of Radar, 2nd' Ed. McGraw-Hill (1946).
109. PB21937, War Dept., Radar Signal Generator TS-155B/UP on 2700-2900 Me.*
11®. PB23432, War. Dept.» Range Calibrator 1-146.
111. PB23625, R. E. Darrell, Pulse Voltmeter Design and Analysis.
112. PB24921, Navy Dep*,, PPI repeater VD.
i?f" £H!?SJ' 1*4 ^fe S^ct^im .a.najy?er for Pulsed oscillators at 3000 Me.
U4=. FB32786^ Bnttou Chance, Precision Time Calibrator and Range Measuring System.
BIBLIOGRAPHY 9-33
Pulse Tubes
121. R. L. Sproull, An Investigation of Short-time Thermionic Emission from Oxide-coated Cathodes,
Phys. Rev., Vol. 67, 166 (March 1943).
122. Editor, Cavity Magnetrons, Electronics, Vol. 19, No. 1, 126-131 (January 1946).
123. H. G. Shea, Theory of Magnetron Tubes and Their Uses, Elec. Ind., Vol. 5, No. 1, 66-70
(January 1946).
124. J. H. Findlay, Design and Construction of Radar Series Spark-gap Tubes, Elec. Mfg., Vol. 37,
No. 3, 131-132 (March 1946).
* 125. J. B. Fisk, H. D. Hagstrum, and P. L. Hartman, The Magnetron, as a Generator of Centimeter
Waves, B.S.T.J., Vol. 25, 167-348 (April 1946).
126. J. T. Randall, The Cavity Magnetron, Proc. Phys. Soc., May 1, 1946, pp. 247-252.
* 127. R. R. Law, D. G. Burnside, R. P. Stone, and W. B. Whalley, Development of Pulse Triodes
to Give 1 Megawatt at 600 Megacycles, R.C.A.. Rev., Vol. 7, 253-264 (June 1946).
128. M. Levy, Power Pulse Generator, Wireless Eng., Vol. 23, 192-197 (July 1946).
* 129. Harold Heinst Hydrogen Thyratrons, Electronics, Vol. 19, No. 7, 96-102 (July 1946).
130. E. A. Coomes, The Pulsed Properties of Oxide Cathodes, J. Applied Phys., Vol. 17, 647-657
(August 1946).
1. J. J. G '
131. J. J. Glauber, Radar Vacuum-tube Developments, Elec. Comm., Vol. 23, 306-319 (September
1946).
132. Lloyd P. Hunter, Energy Build-up in Magnetrons, J. Applied Phys., Vol. 17, 833-843 (October
1946),
133. PB28647, R. C. Fletcher and G. M. Lee, Preliminary Studies of Magnetron Build-up.
Timing Circuits and Relaxation Oscillators
* 141. H. J. Reich, Trigger Circuits, Electronics, Vol. 12, No. 8, 14 (August 1939).
* 142. O. S. Puckle, Time Bases. John Wiley (1943).
143. F. E. Terman, Radio Engineers1 Handbook, pp. 511-516. McGraw-Hill (1943).
* 144. Navy Dept., Timing Circuits, Navships 900,013 (May 1944).
145. M. V. Kiebert and A. F. IngUs, Multivibrator Circuits, Proc. I.R.E., VoL 33, 534-539 (August
1945) . (Calculation of period from time constants.)
* 146. D. McMuUan, A Single Sweep Time Base, Electronic Eng., Part 1, VoL 65, No. 1, 21-23
(January 1946); Part 2, VoL 65, No. 2, 47-50 (February 1946).
147. L. B. Tooley, Gate Circuits for Chronographs, Electronics, VoL 19, No. 5, 144-145 (May 1946).
148. R, Stang, The Blocking Oscillator, Radio News, VoL 36, No. 3, 14-15, 20 (September 1946).
I>elay Lines
151. J. P. Blewett and others, Delay Lines. General Electric Co. reports (1943).
152. M. J. DiToro, Delay Lines. Hazeltine Electronics Corp. reports (1945).
153. M. G. E, Golay, The Ideal Low-pass Filter in the Form of a Dispersionless Lag Line, Proc.
I.R.E., VoL 34, 138P-144P (March 1946).
154. J. M. Lester, Transient Delay Line, Electronics, VoL 19, No. 4, 147-149 (April 1946).
155. H. E. Kallmann, High-impedance Cable, Proc. I.R.E., VoL 34, 348-351 (June 1946).
156. H. E. Kallmann, Equalized Delay Lines, Proc. I.R.E., VoL 34, 646-657 (September 1946).
157. K. H. Zimmerman, Spiral Delay Lines, Elec. Comm., VoL 23, 327-328 (September 1946).
Pulse Transformers
161. H. A. Wheeler, Formulas for the Skin Effect, Proc. J.R.E., VoL 30, 412-424 (September 1942).
162. R. Lee, Iron-core Components in Pulse Amplifiers, Electronics, VoL 16, No. 8, 115-117, 262-268
(August 1943).
* 163. A. G. Ganz, Permalloy Tape in Wide-band Telephone and Pulse Transformers, Elec. Eng.,
VoL 65, Trans., pp. 177-183 (April 1946).
164. PB32773, J. W. Dunifon, Pulse Transformers.
Computers
171. J. T. Potter, A Four-tube Counter Decade, Electronics, VoL 17, No. 6, 110-113, 358, 360 (June
1944).
172. Editor, Preset Interval Timer, Elec. Ind., VoL 4, No. 7, 97-99, 130, 134, 138, 142, 146 (July 1945).
173. V. H. Regener, Directly Coupled Pentode Trigger Pairs, Ret). Sci. Instr., VoL 17, 180-184 (May
1946). Decade Counting Circuits, 185-189.
174. A. W. Burke, Super Electronic Computing Machine, Elec. Ind., VoL 5, No. 7, 62-67, 96 (July
1946).
175. H. G. Shea, Electronic True Decade Counters, Elec. Ind., VoL 5, No. 9, 82-84, 136 (September
1946).
176. A. Kip, A. Bousquet, R. Evans, and W. Tuttle, Design and Operation of an Improved Counting
Rater Meter, Ret. Sci. Instr., VoL 17, 323-333 (September 1946).
177. B. E. Watt, Current Integrator, Rev. Sci. Instr., VoL 17, 334-338 (September 1946).
178. A. G. Bousquet, Radioactivity Meter for Nuclear Research, Elec. Ind., VoL 5, No. 9, 88-89
(September 1946).
179. I. E. Grosdoff, Electronic Counters, R.C.A. Rev., VoL 7, 438-447 (September 1946).
180. V. H. Regener, Reversible Decade Counting Circuit, Rev. Sci. Instr., VoL 17, 375-376 (October
1946).
* 181. R. R. Batcher and William Moulic, The Electronic Control Handbook. CaldweU-Clements
(1946). Section 3, Chapter 3, Counting and Timing Controls, pp. 178-195, 338.
182. S. A. Karff, Electron and Nuclear Counters. Van Nostrand (1946).
Picture Transmission
* 191. RCA, Television, VoL 1 (July 1936); Vol. 2 (October 1937).
* 192. J. C. Wilson, Television Engineering. Sir Isaac Pitman & Sons, London (1937). Chapter 12,
Physical Limitations, pp. 420-437.
9-34 PULSE TECHNIQUES
193. J. C. Wilson, Channel Width and Resolving Power in Television Systems, J. Television Soc.,
Vol. 2, 397-420 (June 1936).
* 194. RCA, Radio Facsimile, Vol. 1 (October 1938).
* 195. V. K. Zworykin and G. A. Morton, Television. John Wiley <1940).
* 196. National Television Svstems Committee, Television Standards and Practice (1943).
* 197. C. E. Dean, Television Principles. Hazeltine Electronics Corp. (1944).
Pulse Modulation for Communication
201. R. A. Heising, Transmission System, U. S. Pat. 1,655,543T April 18, 1924-Jan. 10, 1928.
202. R. H. Ranger, Reproducing and Transmitting Pictures, U. S. Pat. 1,848,839, Feb. 26, 1924-
March 8, 1932.
' 203. J. L. Finch, Signaling System, U. S. Pat. 1,887,237, May 31, 1929-Nov. 8, 1932.
204. R, D. Kell, Signaling System, U. S. Pat. 2,061,734, Sept, 29, 1934-Nov. 24, 1936.
205. lW. R. Koch, Secret Communication System, U. S. Pat. 2,199,634, June 21, 1938-May 7, 1940.
206. D. G. C. Luck, Signaling System, U. S. Pat. 2,227,596, March 31, 1938-Jan. 7, 1941.
207. Bertram Trevor, Pulse Signaling System, U. S. Pat. 2,361,437, Dec. 4, 1940-Oct. 31, 1944.
* 208. E. M. Deloraine and E. Labin, Pulse-time Modulation, Electronics, VoL 18, No. 1, 100-104
(January 1945).
*209. E. M. Deloraine and E. Labin, Pulse-time Modulation, Elec. Com., Vol. 22, 91-98 (1944).
210. Editor, Pulse Position Modulation Technique, Elec. Ind., Vol. 4, No. 12, 82-87, 180, 182, 184,
186, 188, 190 (December 1945).
211. D. D. Grieg, Multiplex Broadcasting, Elec. Com., Vol. 23, 19-26 (March 1946).
212. F. F. Roberts and J. C. Simmons, correspondence, Wireless Eng., Vol. 23, 93 (March 1946).
* 213. J. J. Kelleher, Pulse-modulated Radio Relay Equipment, Electronics, Vol. 19, No. 5, 124-129
(May 1946).
*214. D. D. Grieg and A. M. Levine, Pulse-time-modulated Multiplex Radio Relay System-terminal
Equipment, Elec. Com., Vol. 23, 159-178 (June 1946).
215. Editor, Multi-channel Pulse Modulation, Wireless World, Vol. 52, 187-192 (June 1946).
216. D. I. Lawson, A. V. Lord, and S- R. Kharbanda, Transmitting Sound on the Vision Carrier
of a Television System, J. I.E.E., Part III, Vol. 93, 251-274 (July 1946).
217. W. R. Greer, Pulse Modulating System, Electronics, VoL 19, No. 9, 126-131 (September 1946).
218. D. G. Tucker, Pulse Distortion: Interchannel Interference in Multichannel Systems, J. I.E.E.,
VoL 93, 323-334 (September 1946).
219. H. S. Black, J. W. Beyer, T. J. Grieser, F. A. Polkinghorn, A Multichannel Microwave Radio
Relay System, Elec. Eng., VoL 65, 798-805 (December 1946).
* 220. RCA, Television, VoL 3 (December 1946); VoL 4 (January 1947).
221. Airborne Radar Specifications, Electronics, Vol. 20, 132 (February 1947).
222. D. G. Fink, Principles of Television Engineering, McGraw-Hill (1947).
* 223. D. G. Fink, Radar Engineering, McGraw-Hill (1947).
224. Harvard Univ., Electronic Tubes and Circuits, McGraw-Hill (1947).
225. Reuben Lee, Electronic Transformers and Circuits, John Wiley (1947).
226. W. M. Goodall, Telephony by Pulse Code Modulation, Bell Sys. Tech. J., Vol. 26, 395-409
(July 1947).
227. R, W. Sears, Electron Beam Deflection Tube for Pulse Code Modulation, Bell Sys. Tech. J.,
VoL 27, 44-57 (January 1948).
228. L. B. Arguimbau, Vacuum-tube Circuits, John Wiley (1948).
229. Australia, Textbook of Radar, Chapman & Hall (1948).
23D. S. Goldman, Frequency Analysis, Modulation and Noise, McGraw-Hill (1948).
231. E. C. Pollard and J. M. Sturtevant, Microwaves and Radar Electronics, John Wiley (1948).
232. R. Q. Smith, Radio Aids to Navigation, Macmillan (1948).
233. Denis Taylor and C. H. Westcott, Principles of Radar, Macmillan (1948).
234. C. E. Shannon, A Mathematical Theory of Communication, Bell Sys. Tech. J., VoL 27, 379-
423, 623-656 (July, October 1948).
235. B. M. Oliver, J. R. Pierce, and C. E. Shannon, The Philosophy of Pulse-code Modulation,
Proc. I.R.B., VoL 36, 1324-1331 (November 1948).
236. C. E. Shannon, Communication in the Presence of Noise, Proc. I.R.E., VoL 37, 10-21 (January
237. H. Goldberg and C. C. Bath, Multiplex Employing Pulse-time and Pulsed-frequency Modula-
tion, Proc. I.R.E., VoL 37, 22-28 (January 1949).
238. A. W. Friend, Theory and Practice of Tropospheric Sounding by Radar, Proc. I.R.E., Vol. 37,
116-138 (February 1949).
239. J, H. Dewitt, Jr., and E. K. Stodola, Detection of Radio Signals Reflected from the Moon
Proc. I.R.E., VoL 37, 229-242 (March 1949).
240. W. G. Tuller, Theoretical Limitations on the Rate of Transmission of Information Proc
I.R.E., Vol. 37, 468-478 (May 1949).
241. E. M. Deloraine, Pulse Modulation, Proc. I.R.E., VoL 37, 702-705 (June 1949).
* 242. M.I.T. Radiation Laboratory Series. 28 volumes. McGraw-Hill.
SECTION 10
TRANSMISSION CIRCUITS
WIRE TRANSMISSION LINES
ART BY JOHN D. TAYLOR PAGE
1. Types of Communication Transmission
Circuits 02
2. Frequency Spectrum 02
3. Electrical Characteristics 02
4. Equivalent Networks 08
WAVE GUIDES — THEORY
BY S. A. SCHELKUNOFF
5. Modes of Transmission 09
6. Propagation Constants of Ideal Wave
Guides 10
7. Rectangular Wave Guides 11
8. Circular Wave Guides 13
9. Wave Guides of Arbitrary Cross-Section 15
10. Special Characteristics of Wave Guides 15
11. Wave-guide Discontinuities 16
WAVE-GUIDE COMPONENTS
BY GEORGE L. RAGAN
12. Wave-guide Characteristics 17
13. Flexible Wave Guides and Coupling
Units 18
14. Wave-guide Connectors 19
15. Bends, Twists, and Angles 21
16. Impedance Matching and Impedance
Transformers 22
17. Transition Units 24
18. Motional Joints 26
19. Other Components 28
TRANSMISSION IN SPACE
ART. ^T ^* G. SCHELLENG PAGE
20. Wave Propagation and General View of
the Radio Spectrum 29
21. The Ground Wave 31
22. The Sky Wave 37
23. Obstacles to Transmission 42
24. Range of Radio Stations and Broadcast
Coverage 47
MECHANICAL FEATURES OF
TRANSMISSION LINES
BY JOHN D. TAYLOR
25. Transmission-line Construction 49
26. Electrical Protection of Transmission
Lines 58
27. Cable Sheath Corrosion 63
COORDINATION OF COMMUNICATION
AND POWER SYSTEMS
BY JOHN D. TAYLOR AND
HOWARD L. DAVIS, JR.
28. Foreign Wire Relations 67
29. Structural Coordination 68
30. Inductive Coordination 73
31. Noise Frequency Induction 74
32. Noise Induction Mitigation 82
33. Low-frequency Induction 88
10-01
TRANSMISSION CIRCUITS
WIRE TRANSMISSION LINES
By John D. Taylor
1. TYPES OF COMMUNICATION TRANSMISSION CIRCUITS
Wire communication circuits are classified in two groups, open (bare) wire and cable.
Each group includes a number of different gages and types of wire, and the electrical char-
acteristics of each gage and type are different. Both groups have their respective fields of
use, and frequently these fields overlap and supplement each other. Open wire is generally
economical where the circuit requirements are relatively small and cable costs would be
prohibitive. Cable is desirable and economical where large groups of circuits and the
higher-frequency types of services are involved, and where maximum protection from
surface interferences is essential.
Cable is also employed for specific applications; for example, coaxial cable for television
and radio transmission lines.
2. FREQUENCY SPECTRUM
Communication intelligence and signals (with the exception of those d-c signals used in
telegraph, emergency, control, and other services) are usually transmitted between points
in the form of a-c electrical energy or wave propagation of definite frequencies or frequency
ranges. Because of the different devices for and methods of generating and transmitting
these various a-c frequencies, and in order to avoid interference between the numerous
circuits and services, frequency allocations have been determined for the various classes
of communication and signal facilities.
Communication services may be classified, for the purpose of assigning suitable facilities,
according to the frequency range within which they operate. Figure 1 is a chart of fre-
quencies employed in power and eornrminication services up to about 5 me. (See Sect. 17,
art. S.)
3. ELECTRICAL CHARACTERISTICS
Primary constants of wire lines consist of resistance r in ohms, inductance L in henries,
capacitance C in farads, and leakage conductance g in mhos. For convenience, L, C, or g
may be expressed in smaller units, such as microfarads (millionths of a farad) for C.
These constants vary differently for different wire materials, sizes, spacings, insulation,
conductivity, temperature, and moisture conditions, as well as for different types of
construction, as indicated in Table 1.
Secondary constants are values derived from primary constants; for communication
purposes, they consist principally of (1) impedance z in ohms and phase angle, (2) propaga-
tion constant, composed of the attenuation and wave length constants, (3) wave length,
(4) velocity of propagation, and (5) cut-off frequency. From the various constants, the
electrical characteristics of the different wire lines have been determined, and these char-
acteristics are useful in considering the suitability of such lines for communication purposes
and in the engineering of the wire communication plant.
The secondary constants, expressed in terms of the primary constants, are as indicated
in the following equations. These equations apply to uniform lines of infinite length or
terminated in their characteristic impedances.
CHARACTERISTIC IMPEDANCE, Z0 Z 0. A wire transmission line has both series
impedance, z, and shunt admittance, y. For a line of uniformly distributed primary con-
stants and of infinite length z = r -f JcaL and y = g -f- jtoC, where or (angular velocity) =
2x/ radians [1 radian = (360/2*0 °}.
ZQ — A/f = -\/ — ' ^^ ohms (1)
V* V + oK? ^;
and
r
10-02
ELECTRICAL CHARACTERISTICS
10-03
& «
li
IJ
-
•a i
a ns
<!
+
-ill
s
« o
«j m o — CN — o — oo -- u-\ooco-«J-<s
r>^vr^OCT^r«^ t>iCO — o*«\t>.ooof>li>^
r^ vo ^ o -*• ^ co cc >r — o 06 •«• -^ o
38SSSSS
5 O O O O O C3
«Ar>»<<\"4-ooct4ci"\r*jr>.—
— O <<v ^S **• "^ cO en, -^ -<f
OOOOOOO OOOC2OOOOOO
li
—
— rsj m <N in PS «^v
3 S O O O O O
5 O O O O O C3
||| §§| g
OOOOOOO OOOOOOOOOO
— — o^m — o
eo — ^- 1^ cv fs t>, oo
2 fl< C
b cb -
iA'
: :- =1 i| !| =
3 °
I 1
<4-4 *->
0 'i.
1 !
.a -a
-§
g44§f
10-04
TRANSMISSION CIRCUITS
For standard non-loaded telephone cable lines, L and g are relatively small, so that for
approximate computations these constants may be neglected and
(2)
— /45° ohms
For lumped loaded cable lines (the usual method of loading such lines), the midsection
characteristic impedance ZQ of an infinite loaded line may be determined from a pi net-
work, converted to a T network, which is electrically equivalent to the combined jumped
and distributed constants of a complete loading section of the line. The a (series) and
TELEPHONE
SIGNALING
STANDARD FREQUENCY FOR FORMER
RINGING TELEPHONE BELLS STANDARD
AND SIGNALING OVER LOCAL FREQUENCY FOR
TELEPHONE UNES AND SHORT RINGING OVER
TOLL LINES NOT EQUIPPED SHORT TOLL
WTTH COMPOSITE SETS LINES t
i *
STANDARD FREQUENCY FOR RING-
ING OVER CARRIER CIRCUITS AND
LONG TOLL LINES. SIGNALING CUR-
RENT IS INTERRUPTED 20 TIMES
OPERATION BY VOICE CURRENTS
FREQUENCY
IN CYCLES
PER SECOND
. i
L.
(M (U 1
\ ^T <f
ool 1 1 8 1 ,
,1 ' '8
8? 1
1 ! 1
8§§ | § |§
* T T r
TELEPHONE
f
ORDINARY TELEPHONE TRANSMISSION
PROGRAM TRANSMISSION
VOtCE- FREQUENCY TELEPHONE
ABSOLUTE LIMITS OF AUDIBILITY EXTEND
FROM ABOUT 16 CYCLES TO 32,000
CYCLES, BUT ALL ESSENTIAL FREQUENCIES
FOR SPEECH LIE WITHIN MUCH NARROWER BAND
TELEGRAPH
OEOtMARY TELEGRAPH CAREER TELESRAPH
AS MANY AS to TWO-WAY VOICE-FREQUENCY
NEUTRAL AND POLAR SYSTEMS,. TELEGRAPH CHANNELS MAY BE CARRIED ON
GROUNDED OR METALLIC. AL- BROAD-BAND CARRIER OR FOUR-WIRE CABLE
THOUGH THEORETICALLY EMPLOY- FACIUTJES. WHERE BAND WIDTH OF FACILITIES
tNG DIRECT CURRENT, TELEGRAPH IS RESTRICTED, FEWER CHANNELS ARE POS-
TRANSM*SSJON INVOLVES A-C SIBLE. THESE BLOCKS MAY BE SUPERIMPOSED
FREQUENCIES RANGING UPWARDS ONE ON TOP OF THE OTHER BY DOUBLE MOO-
TO ABOUT 25 CYCLES ULATHDN TO UTILIZE ANY AVAILABLE FREQUEN-
( * 1 CY RANGE
f 1
[
FREQUENCY
IN CYCLES
PER SECOND
2 !!
1
3 S f
1 1
: § s
til 1
SS88I 8 § |
1 ill 1
§O O O O <
1 § III
1 f 1
i 1 1 o
i 7*
PO^^
?IAJJSff° POW€R TRAMS -V^ STANDARD FREQUENCY
J£fSJ?!LWHE*' ^TERNAT- USED MOST EXTENSIVELY
INC CURRENT RAILWAYS IN POWER WORK
INC IS A SECONDARY CON~-
Sl DERATION
FIG. 1. Operating Frequencies for Power and
ELECTRICAL CHARACTERISTICS
& (shunt) values of the T network having thus been determined,
10-05
(3)
For uniform or lumped loaded cable lines at voice frequencies coL is large with respect to
r and
ohms
(4)
°1T<MJ1J? f 777 TTTTTir ? ?7? 7
{fti !!!!
**"
n " LONG -WAVE ^ f
TRANSATLANTIC A
TELEPHONE QRCUITS T
fS^METERS-*s|
BROADCASTING
COAXIAL
CABLE
FIXED AND MOBI-LE RADIO TELEPHONE BANt>S AS ALLOC
AUTHORITY THROUGH THE RANGE FROM tO KILOCYCLES T
E TO W AND W TO E
ATED BY GOVERNMENTAL
3 30,000 MEGACYCLES
RADIO TELEPHONE L,.
SHORT-WAVE TRANSOCEANIC ''
TELEPHONE CIRCUITS
(4 TO 22 MEGACYCLES)
> CARR.IER TELEPHONE
TYPE K trninnnnnrgnmnn CABL \ SYSTEM
1 2 3 4 5 6 78 10 12
WTOE ETOW OPEN-WIRE SYSTEMS
TYPE H
ETO WAND WTOE
TYPE G | "' | W TO E E TO W
* TYPE jDOJODDDOODBO^ir
WTOH ETOW 1 6 12 12 1
rrnf'rnr
TVO^' LJI TYPE M | |
= TOW WTOE ^CA^IfS
*TYPEC | 111 11 fl QDQ
321213
RADIO TELEGRAPH
F XED AND MOBILE RADIO TELEGRAPH
BANDS AS ALLOCATED BY GOVERNMENTAL
AUTHORITY THROUGH THE RANGE FROM
10 KILOCYCLES TO 30,OOO MEGACYCLES
§ | ||| |
iiil ||i}
i
NOTE: LIGHTNING FREQUENCIES RANGE FROM A FEW HUNDRED THOUSAND TO THE HIGHEST
FREQUENCIES AND ARE INVOLVED IN THE ENGINEERING DESIGNS OF PROTECTION IN
BOTH POWER AND COMMUNICATION WORK
* THESE REPRESENT THE FREQUENCY ALLOCATIONS FOR ONE SYSTEM OF THIS TYPE ;
OTHERS ARC DISPLACED SLIGHTLY, OR EMPLOY OTHER SIDEBAND
Communication Services (Courtesy Bell System)
10-06 TRANSMISSION CIRCUITS
For non-loaded open wire lines at radio frequencies
2D
ZQ = 276 logic —r ohms (5)
a
where D is the distance between the centers of the wires and d is the diameter of the wires-
For coaxial (concentric tube; cable lines at carrier and higher frequencies
Zg == 138 logio - ohms (6)
a
where a is the outer radius of the inner conductor and b is the inner radius of the outer
conductor.
PROPAGATION CONSTANT. The propagation constant, 7, is a function of the series
impedance, 2, and the admittance, y, in the vector relation
-j«C) (7)
Also, 7 is composed of an attenuation constant a and a wave length constant /3 in the
relation
7 = a. + j8 = y cos 8 + 37 sin 9 (S)
where / - , -
a - V Va vV + «W)tf -f or'C*) + 1/2 («r - o>2LC) (8a)
0 » V Vs "V "(r2 + ftWjtf + ^C2) - 1/2 (& - <£LC} (86)
Equation (S&) gives a in nepers (1 neper = 8.6S6 db)T and eq. (86) gives £ in radians
(1 radian — 57.296°). It is usually more convenient to calculate a and /? from eqs. (7)
and (8) than from eqs. (8a) and (86).
From the above discussion it is seen that the propagation constant represents both the
dying-away and phase-change effects of the voltages and currents, as they progress along
the line.
If y is given for 1 mile, then the total attenuation and phase change effects for I miles
is £7. The ratio of the current 7s at the receiving end to the current Ji at the sending end
of a uniform line, I miles long and properly terminated, is
*j = 8 -*y = e-i<«+#> = e-?«/^ (9)
Thus, the magnitude of h = /i8~ la and the two currents differ in phase by the angle Z£»
which is expressed in radians.
From Eq. (9)
2.303 logiey -- la
h
and the magnitude of the propagated current I*, in terms of the sending current Ji, at
any point along a uniform transmission line, is
h „ l (10)
Ii , -j la
10810 2J03
Also, if P2 is the received power and EI and h are the sending end voltage and current,
respectively, with phase angle B, then
t-*1* cos $ (11)
showing that the power is attenuated in accordance with the square of the current ratio.
If the constants of the transmission line are such that r/L = g/C or rC — Lg, then the
line attenuation and velocity of propagation do not change appreciably with frequency
and the line is said to be dwtortionfes», since
For standard non4oaded telephone cables, L and g are considered negligible: hence
from eqs. (S) _ ^^
a == £ = '\~- nepers (for a} and radians (for £) (13)
For uniformly or lumped loaded cable lines (up to about mid-frequency range) where
r and g are small compared to uL and o><7 respectively, an approximate expression for
o; 28
£ + i| nepers (14)
ELECTRICAL CHARACTERISTICS 10-07
In this equation, r/2L and g/2C are the damping constants of the series and shunt con-
stants, respectively, of the line.
If g is assumed to be zero, eq. (14) becomes
_/"r
nepers (15)
Equation (15) also applies for open-wire lines in the r-f range.
Thus, it is seen from eqs. (13) and (15) that, for values of (r/2L) < co, a. is decreased by
increasing L, i.e., by loading the cable line, although the full advantage is not realized,
because, in loading the line, r is increased slightly by the resistance of the loading coils.
For coaxial (concentric tube) cable lines in the r-f range
(16)
and, where both conductors are of the same material and the line dimensions are available,
1/6) . 1Q-, neper per unit length (17)
276 logio(6/a)
where p = resistivity of conductors in emu (about 1730 emu for pure copper).
fi — magnetic permeability of the insulation.
/ = frequency in cycles per second.
a = outer radius of the inner conductor.
b — inner radius of the outer conductor.
WAVE LENGTH. The phase of the voltage and current for a uniform line is contin-
ually changing in a modified sine-wave pattern, as progression takes place along the line.
A complete phase change of 2?r radians (360°) will occur in the length of line traversed by
the voltage and current during the time they pass through 1 cycle. Thus, the wavelength
X for a particular line may be equated as
2r
X = -— miles (18)
P
& being the phase change in radians per mile.
VELOCITY OF PROPAGATION. Since a wave length is the length traversed by the
voltage and current during 1 cycle, the velocity of propagation W may be equated as
W = X/ miles per second (19)
/ being the frequency in cycles per second.
For loaded cable lines, the inductance and capacitance of the line have a direct bearing
on the wave length constant, wave length, and velocity of propagation. Since r and g are
usually negligible for such lines, eq. (86) for /3 becomes
|8 = coVZc = 2-n-fVLC (20)
Since X - 2w/fr
97T/ 1
W = X/ = — - = — = miles per second (21)
0 VLC
Note: If L and C are expressed as the values for one load section, then /3 and X are in
loads and W is in loads per second.
CUTOFF FRE QUENCY. For non-loaded lines (cable or open wire) , the cutoff frequency
is usually high enough for all practical purposes for the service for which these facilities
will be used, but for loaded cable lines the cutoff frequency is an important factor and may
be expressed as
fc - — ~ (22)
irVLC
where L is the inductance of the loading coil in henries and C is the capacitance of the
loading section in farads for any particular line.
Thus, the periodic lumped loaded line transmits all frequencies up to a critical or cutoff
frequency. However, in the actual line there are some deviations from the ideal loading
and some resistance in the line and loading coils, resulting in the attenuation of the trans-
mitted frequency range to some degree.
10-08
TRANSMISSION CIRCUITS
4. EQUIVALENT NETWORKS
Equivalent networks for a length of uniform line, transmitting alternating currents, may
be constructed in the T or pi (TT) form.
For the T network, a, the value of each of the two series arms, and 6, the value of the
shunt arm, may be obtained from the equations
(23o)
& = -7^~r (236)
smh ly
where ZQ, I, and y are the characteristic impedance, length of line in miles, and the propaga-
tion constant per mile.
ly
a — Z0 tanh — -
8
-- 10
--8
€
5
-- 5
4
3
2
J2
S^
x**^
^X"
^
^x"
^
•"'
.
* ^
x*
^
"?*
^
i*
^1
0
3
T:
I
)2
Mils.-
^
^
X
,>'
**
x
x*
x
^
-- 1
~~~^6~
B. £
r>d
s
1
b2
i^
--^d_
p?
x: —
._ x^-
X"
--0.8
-° n c
(-
X
N
yX"
^ «•*'
jf
-0.5
-0.4
^0.3
Jo.2
0.1
xx^
s^x*^
^
^s*^
• ~ 0.6
x
I**1
j
^x
^
^x
^*-
jjx^
(x
^x*
^
^^
^x"
(
x
^s*
^
^.
.
X*^^
x^
Lx-1
pX
^
x^
N
rfjOE
. 3r
dS. 32S
Ml
s.
^
^x""
x
Lx
x
•S
\
X*
-*
x
L-
x
•"•
x-
\s
X
rt'c
>000
3. a
(IS. 46<
M-
s.
•-0.1
0.08
O.C6
0.05
-x^^
__
•^
--0.08
^x
^x**
^
-="
--0.05
0.04
0.03
0-
XI
-f-f 1
--0.04
i [
05 0.1 O.2 0.3
0.5 1 23
5
10 20 30
50
Frequency - Megacycles per Second
FIG. 2. Calculated Attenuation vs. Frequency Characteristics, 600 ohm, Two-wire lines, Solid Copper
Conductors ; Leakage and Radiation Neglected
For the pi network, r, the value of each of the two shunt arms, and s, the value of the
series arm, may be obtained from the equations
r = jZ^o coth —
2
« = ZQ sinh Z-y
(24a)
(246)
where Z& Z, and y have the same meaning as for the T network.
Figure 2 shows the calculated attenuation-frequency characteristics of 600-ohm, two-
wire, solid copper lines, in which leakage conductance and radiation are assumed to be
negligible. Calculations are based on the equation
= S.686 -
10 "* decibel per mile
(25)
radii of the various conductors in miles, / = megacycles per second, and ZQ =
ic impedances of the various lines. The effect on current distribution of the
(important only when the ratio of separation to wire diameter is less than 20
to 1) is neglected in the equation.
MODES OF TRANSMISSION
10-09
Figure 3 shows the calculated attenuation-frequency characteristics of copper concentric
tube lines having optimum ratios of conductor radii. Leakage is neglected. Calculations
are based on eq. (17). Assuming both conductors to be of the same material, a. will be
1UU
SO
60
50
-f-
J
-- 50
40
30
20
m 10
-; 40
JX
x
x*
x^
<^^
x
'*
'
x^
^
-; 10
s *
1 6
x
1
x"*
-- 8
^x"
x
x
. _ &
f*^" —
0.1
25
in
•*'
^
-- 5
1 4
o 3
J 2
£
< 1
r~n
^i
x
^.x
^
^
.X
x
. ^
x
L*"
s<^
''
X
Ix"
x<
---0.25j
in.
x
*^
x*
X*
,,^
x"'
^
X^
x^
x^
-"
'x
x-"
x*
x
x'*
x*^^
5 'in
^
x*
-I
0.8
0.6
0.5
0.4
0.3
0.-2
0.1
0.
-_^X— —
~?
" —
*--
- - Ct ft
x
^
X
x
x
x
x^
• - 0-Q
x^1
^
<-
-1
5
'n
- - 0 5
--04
x
^^
s>
^x1
--03
^
x'
^x
•"'
-no
^
x''
X
•''
.- OJL
05
0.1 0.2 0.3 0.5
1 23 5 ' 10 , 20 -.30
50
Frequency - -Megacycles per Second
FIG. 3. Calculated Attenuation vs. Frequency Characteristics, Copper Concentric Tube Lines.
Optimum ratio of conductor radii. Leakage neglected. Dimension indicated is inner radius of
outer conductor.
a Tni-nimiiTn when the ratio b/a
reduced to
3.6. With p ~ 1730 and a a minimum, eq. (17) can be
. 0.686V/
decibels per mile
(26)
where / is in megacycles per second and b is the inner radius of the outer conductor in
inches.
WAVE GUIDES— THEORY
By S. A. Schelkunoff
Definition. A wave guide is a structure consisting of either conductors or dielectrics,
or both, in which the boundaries between different media are cylindrical (surfaces made
up "by a translation of a straight line; circular cross-section is not essential). A meted wave
guide is a wave guide containing at least one conductor. A dielectric wave guide is a wave
guide consisting of dielectrics only.
5. MODES OF TRANSMISSION
Three types of waves are possible in straight metal wave guides filled with a homogeneous
dielectric: transverse electromagnetic or TEM waves, transverse electric or TE waves,
and transverse magnetic or TM waves. In TEM waves the electric and magnetic vectors
10-10 TRANSMISSION CIRCUITS
are perpendicular to the direction of the guide; in, TE waves the electric vector is so dis-
posed; and in TM waves the magnetic vector is perpendicular to the guide. TEM waves
are possible only if the guide consists of two or more separate conductors; there are no
restrictions on the existence of the other types. If the dielectric is non-homogeneous, then
in general the waves are of hybrid type, with all components of E and H vectors present.
Each wave guide permits an infinite number of transmission modes. Besides the above-
mentioned general characteristics, each mode is distinguished by a transverse field pattern
consistent with the structure of the guide. Theoretically, at least, it is possible to excite
an arbitrary field pattern over a given cross-section of the guide; but, in general, this
pattern will not be maintained along the guide. The self-maintaining patterns are the
ones that define the various modes of transmission. In general, these patterns depend on
the frequency as well as the structure of the wave guide; but, if the dielectric is homoge-
neous, then the patterns are independent of the frequency and are given solely by the
geometry of the metal boundaries. Each self-maintaining pattern is either attenuated or
is traveling with a phase velocity peculiar to it. (See Propagation Constants, article 6.)
An arbitrary pattern excited over a given cross-section breaks up into self-maintaining
patterns. The field at various distances from the source is the result of interference be-
tween the self-maintaining patterns arriving with different amplitudes and phases.
In wave guides with rectangular, circular, and elliptic boundaries, the various TE and
TM modes are designated by a double subscript, TEmn and TMmn, where m and n are
integers appearing in the mathematical functions describing transverse field patterns.
For each shape of the guide, indices m and n reflect certain physical characteristics of the
wave; but the same indices for different shapes correspond to waves with different charac-
teristics, and waves with similar characteristics may have different indices. This happens
because a gradual deformation of a circular boundary into a rectangular affects different
modes differently.
In a wave guide of arbitrary shape the various modes are designated by a single subscript
which denotes the position of the "cutoff frequency" on the frequency scale. The dominant
tease is the wave with the lowest cutoff frequency.
6. PROPAGATION CONSTANTS OF IDEAL WAVE GUIDES
For an ideal non-dissipative wave guide with a homogeneous dielectric the propagation
constant yg along the guide for a given transmission mode is
yg = <ocVM£ \1 - ( - ) co = 2*/ (1)
\«C/
where the cutoff frequency fc is determined by the permeability ju and dielectric constant 8
and by the geometry of the boundaries. For / < /c, y is real and the wave is attenuated
even though there is no dissipation of energy. For / > fc the above equation becomes
and the propagation constant is imaginary. The wave becomes active in transmitting
energy to large distances since under the assumed ideal conditions the amplitude of the
wave does not diminish. These characteristics are the characteristics of a high-pass filter.
For wave guides with a non-homogeneous dielectric there is no simple general expression
for the propagation constant.
PHASE VELOCITY. Above the cutoff the phase velocity along the guide is
' Vl - <w«)* = V^ = v£
where v is the intrinsic velocity of the dielectric (velocity of light in the dielectric), c is the
intrinsic velocity of vacuum, and Zr is the dielectric constant relative to vacuum. In
hollow wave guides the phase velocity is always higher than the velocity of light in free
space; this is in keeping with the high-pass characteristics of wave guides.
GROUP VELOCITY. The group velocity or the velocity of a "wave packet" is
(3)
Hie product of the group and phase velocities equals the square of the intrinsic velocity.
RECTANGULAR WAVE GUIDES
10-11
WAVELENGTH IN" THE GUIDE. The wavelength \g in the guide (the distance from
crest to crest of the wave) is
(V/)
Vl -
(4)
where Xr is the free-space wavelength corresponding to the given frequency / and ST is the
dielectric constant relative to vacuum.
7. RECTANGULAR WAVE GUIDES
FIELDS. In a metal wave guide the effect of the conductivity of the walls on the field
distribution is negligible. The following expressions are for perfectly conducting walls,
assuming that the coordinate system is disposed as in Fig. 1. The time factor exp jut is
omitted.
TEmnt wave (if traveling in the positive z direction) :
_ , nir mitx . niry ~
Ex = A -r- cos sin — ; — e r
b a b
By rr E*
KTE
. rrnr . WITTS mry
— A — sin cos —r— e~'s
o, d b
A XmrT rmrx mry
A - — cos cos — - — e "
a b
J&ft
(5)
2 52
where m, n are integers, not equal to zero simultaneously. The quantities g, /z, and 8 are
respectively the conductivity, the permeability, and the dielectric constant of the dielectric
in the guide. Figure 2 shows electric lines for some TE waves; they are also the lines of
constant Hz. The transverse H com-
ponent is perpendicular to the E vec-
tor. The density of lines is propor-
tional to the transverse field compo-
nents. The pattern of the TE1>0
wave in Fig. 2 (a) is the building
block, for patterns of the TEm,o
waves as illustrated in Fig. 2(c);
FIG. 1
Electric Lines in Rectangular Guides; (a)
d)
FIG. 2.
TEi,o Wave; (&) TEi.i Wave; (c) TE2,0 Wave; (
TEo,2 Wave
m is the number of such blocks in the pattern of the TEw,o wave. In the TEo.n wave the
lines are parallel to the horizontal faces of the guide. The pattern of the TEifl wave in
Fig. 2(c) is the building block for the pattern of the TETO,R wave when m and n are different
from zero ; m is the number of such blocks in the x direction (the horizontal direction) , and
n is the number of blocks in the y direction.
TMw,n wave (if traveling in the positive z direction) :
. ttTT . WTTX mry
•• A — sin cos — — e"
b a b
mir m-jrx . nicy
— — A — cos sin
a a o
g -f .70)8 *
(6)
• v
where m, n are integers not equal to zero. Figure 3 shows magnetic lines for some TM
waves; they are also the lines of constant E^. The transverse E component is perpendicular
to the H vector. The density of lines is proportional to the transverse field components.
10-12
TRANSMISSION CIRCUITS
The pattern of the TMi.i wave in Fig. 3 (a) is the building block for the pattern of the
TMm,n wave; m is the number of such blocks in the x direction, and n is the corresponding
number in the y direction.
CUTOFF FREQUENCIES. The cutoff frequencies for the various modes of trans-
mission are the frequencies at which the propagation constant vanishes; at these fre-
quencies the propagation constant changes
from a real to an imaginary value; these
frequencies separate the pass band of fre-
quencies from the stop band. In this sense
the cutoff frequencies are defined only for
non-dissipative wave guides; the cutoff fre-
quencies of slightly dissipative wave guides
are usually denned by neglecting dissipa-
tion. In general, the cutoff frequency may
be defined as the frequency at which the
Ita. 3.
. ta , ^ctengular_Guides; («>
phase of the propagation constant is 45°; but when the dissipation is really large the
concept of "cutoff" loses its practical value.
For rectangular wave guides the cutoff frequencies and corresponding wavelengths (in
vacuum) are
V U
V(m/a)»
where c is the velocity of light in vacuum.
The same formulas hold of TE and TM waves. For the dominant wave
Xi.o = 2aVev /i,o =
(7)
(8)
where a is the longer dimension of the cross-section of the guide.
ATTENUATION IN THE PASS BAND. In a previous section the exact expression is
given for the propagation constant y when the walls of the guide are perfect conductors.
To allow for the imperfect conductivity of the walls the following correction term should
be added to y
A-y = am(l + j) (9)
where am is the attenuation in nepers per meter due to absorption of energy by the walls.
For TEmn wave
0, n
(i+f'
\ a o
0, n =
« 0, n
(10)
Vhere p — b/a, vmn = /»»„//, and ffi is the surface resistance of the walls, and
(ID
In this equation, ^r is the permeability of the walls relative to vacuum, gm is the conduc-
tivity, and \v is the wavelength in vacuum for the given frequency /. For pure copper,
g — 5.80 X 107 mhos per meter and
(* = 2.61 X 10-
For the TMOT» wave
8.25X H^ \
,.
" ^n }
(12)
(13)
!Hie above formulas for or,,, break down in the immediate vicinity of the cutoff; the
attenuation, does not go to infinity — it is merely large compared to the attenuation else-
wfeere in the pass band (see a later section on the attenuation near the cutoff).
CIRCULAR WAVE GUIDES
10-13
8. CIRCULAR WAVE GUIDES
FIELDS. For the TEn,m wave the cylindrical components of the field vectors are
= A - Jn
p
sin n? e
= A
cos r^ e
where kn,m is the mth non-vanishing zero of the first derivative of the Bessel function
Jnf(k), and a is the inner radius of the guide. Some k's are given below:
&0,i = 3.83 &o,2 = 7.02 &o,3 = 10.17
&i.i = 1.84 &i,2 = 5.33 Jfci.s = 8.54
&2,i = 3.05 &2,2 = 6.71 &2,3 - 9.97
h,i = 4.20 kz.z = 8.02 A3,3 = 11.35
Figure 4 shows electric lines for some TE waves. The electric lines of TEo.m waves are
circles; for this reason TEo.m waves are called circular electric waves.
FIG. 4. Electric Lines in Circular Guides; (a) TEo.i Wave; (b) TEi.i Wave; (c) TE2,i Wave; (d)
TEi,2 Wave; (e) TElfi Wave Between Coaxial Cylinders
For the TMn,m wave the field is
H0 = A - Jn ( -^- ] sin n<p e~
A - Jn
cos n<p e
(15)
Ep =
= -KZ™HP
A/71775
' (g + /<*
g
<\W
where fcnm is the mth non- vanishing zero of the Bessel function /»(&). Some A's are givea
below:
fcotl = 2.40 ^0,2 = 5.52 &o,3 = 8.65
^L,I = 3.83 ^1,2 = 7.02 fo.s - 10.17
fe,i = 5.14 Ar2,2 = 8.42 fe,3 = 11.62
Jfcs,i = 6.38 &s,2 = 9.76 As,s = 13.02
Figure 5 shows magnetic lines of some TM waves. The magnetic lines of TMo.m waves
are circles; for this reason TM0,m waves are called circular magnetic waves.
10-14
TRANSMISSION CIRCUITS
FIG. 5. Magnetic lines in Circular Guides; (o) TM0,i Wave; (&) TMi.i Wave; (c) TMit2 Wave;
(d) TM2,i Wave
CUTOFF FREQUENCIES. The cutoff frequencies and corresponding wavelengths (in
vacuum) are _
(16)
' nm J.
n>nm
where c is the velocity light in vacuum and knm is the quantity denned in the preceding
section. For the dominant wave '
l.7dVsr
(17)
where d is the inner diameter of the guide,
ATTENUATION IN THE PASS BAND. The propagation constant 7 given in a
previous section is for the case of ideal non-absorbing walls. To allow for absorption by
these walls, 7 should be augmented by
A7 = am(l + j) (18)
where an is the attenuation in nepers per meter caused by the absorbing walls. For TE
waves
(18a)
where vnm = /n»//. The surface resistance (R is given in the corresponding section on
rectangular wave guides.
For circular electric waves n — 0 and
,m2(l - *o,m2)-^ (186)
If the dielectric is non-dissipative, the attenuation of circular electric waves steadily
decreases with increasing frequency
For dominant waves (
[3.76(1 - n,!2)-^ - 2.65(1 - Ji.i2)^J10-3 neper/meter
For TM waves
' (X — jrnjB*
SPECIAL CHARACTERISTICS OF WAVE GUIDES 10-15
9. WAVE GUIDES OF ARBITRARY CROSS-SECTION
CUTOFF FREQUENCIES. For wave guides of arbitrary cross-section the cutoff
wavelength, (in vacuum) and the cutoff frequency are given by
X. =
JJ
' JJlgrad T|2 dS
*-s
(19)
where c is the velocity of light in vacuum, and T is proportional either to Ez or to Hz*
depending on the type of the wave. This formula is exact; but generally it is not feasible
to obtain T exactly. However, first-order errors in T lead to second-order errors in \c,
and the formula is extremely useful, especially for estimating the cutoff frequency of the
dominant wave; only a reasonable guess is needed for T (see the next section).
WAVE GUIDES WITH CROSS-SECTIONS OF THE TYPE SHOWN IN FIG.
6(a). For dominant waves in wave guides of the shape shown in Fig. 6 (a) electric lines
run across in the manner indicated in the figure. Such wave guides are essentially pairs
of parallel strips, shunted on both sides with cylinders, Fig. 6(6). Longitudinal magnetic
lines run largely inside the cylinders, in opposite directions. On account of the increased
capacitance in the middle, the cutoff frequency of such a wave guide is lower than that
of a rectangular wave guide. To make an estimate of the frequency we let T — Hz — +1
in one cylinder and T = — 1 in the other. Between the parallel strips we assume that the
longitudinal magnetic flux varies linearly from +1 to — 1; that is, we let T — 1 — (2iX/w),
where w is the width of the strips.
The gradient of T is zero inside the cylinders and (— 2/tc) between the strips. Substi-
tuting in the formula contained in the preceding section, we obtain
(20)
where h is the distance between the strips and 5 is the cross-sectional area of each cylinder.
In the above form, the formula applies even when the cylinders are not circular. The
width w should be comparable to one-half of the total width.
If this formula is applied to a rectangular wave guide whose cross-section is broken up
as in Fig. 7, we find Xi ^ 1.81 a V£T instead of the exact value Xi = SaVe*. The error is
about 10 per cent. The error diminishes as h decreases relatively to other dimensions.
10. SPECIAL CHARACTERISTICS OF WAVE GUIDES
CONDUCTION CURRENT IN THE WALLS OF A WAVE GUIDE. The conduction
current in a metal wall of a wave guide is equal to the tangential magnetic intensity and
is perpendicular to it. The direction is that in which a right-handed screw will advance
when the H vector (which is supposed to be attached to the handle) is turned through 90°
to make it coincident with the normal looking into the wall.
In the case of dominant waves in a rectangular wave guide the current in the walls
parallel to the E vector is strictly transverse. In the other walls the longitudinal current
is sinusoidally distributed, with the highest density in the middle; the transverse current is
zero in the middle and maximum at the edges. In these walls, the transverse current flows
in opposite directions from the middle. As the frequency increases, this current diminishes.
10-16 TRANSMISSION CIRCUITS
ATTENUATION IN THE VICINITY OF THE CUTOFF FREQUENCY. The following
expression for the propagation constant is valid for all frequencies
-y = W + fang + 2a«-yo(l + f) (21)
where 70 is the propagation constant calculated on the assumption g = an = 0. Whereas
am is infinite at the cutoff, amyo is finite. For frequencies not too near the cutoff this
formula is unnecessarily complicated, and it is recommended only for the immediate
vicinity of the cutoff. _
CHARACTERISTIC IMPEDANCES AND POWER TRANSFER. The ratio
Kt = Et/Ht of the transverse components of the E and B vectors is called the wave
impedance. The average power W transferred per unit area of the cross-section of the
wave guide is
W - K2Ht^ (22)
where Ht,en is the effective value of Ht (the factor 1/2 should be included if the amplitude
of fft is being used).
For the dominant wave the total power transfer P is given by
P - Kp.vVet? = Kpjlen* = Kv.iVafctt (23)
where Feff is the effective value of the maximum transverse voltage, 7e« is the effective
longitudinal current, and the K's are the characteristic impedances. For rectangular
wave guides
aVl -
For circular wave guides
764 ^ 354
.
KP,i - , Ky,i = KP,vKp,z (23a)
(235)
Vl -
For wave guides of the shape shown in Fig. 6, approximate formulas are
(23c)
In these formulas P denotes the ratio of the cutoff frequency for the dominant wave to the
operating frequency.
The above expressions may be used without any reservation in power calculations. The
following section should be consulted before any attempt is made to calculate reflections
and standing waves.
11. WAVE-GUIDE DISCONTINUITIES
Any local change in the shape of a wave guide or any obstruction represents a wave-guide
discontinuity. Local fields are likely to be associated with such discontinuities. A capacitor
or a coil shunted across a low-frequency transmission line are examples of discontinuities.
The local fields store energy during one half of the cycle and release it during the other;
they act as virtual generators, operating on power borrowed from the traveling wave. If
the operating frequency is higher than the cutoff frequency of the dominant wave but lower
than the cutoff frequency for any other wave, there is no possibility for the energy to be
sent back to its source or to the load in any mode except the dominant. In these circum-
stances the effect of the local field made up of higher-order waves may be represented by a
reactive transducer which in its turn may be expressed as a T or pi network. The branch
reactances of these equivalent networks may be computed in terms of the reflection and
transmission coefficients if the latter are measured or obtained directly from a solution of
an appropriate electromagnetic boundary value problem. In some special cases the equiva-
lent network reduces to a series or shunt reactance.
If two wave guides of different dimensions are joined together, the junction introduces
a reactive discontinuity of the above-mentioned type as well as a discontinuity in a char-
acteristic impedance to the dominant wave. The reflection coefficient will be determined
not merely by the impedance mismatch but by the reactive discontinuity as well. This
is a general statement, and it applies to ordinary low-frequency transmission lines, for
which, however, the series branches of the reactive discontinuity are so small, and the
sfemut branches so large, that their effect is negligible. In wave guides, on the other hand,
tike e§€Ct is ordinarily not negligible.
WAVE-GUIDE CHABACTEEISTICS
10-17
Some discontinuities are introduced inadvertently, as in joining two wave guides; others
are introduced deliberately as circuit elements. Simplest circuit elements are transverse
diaphragms or irises, Fig. 8 (a), (6), (c), and transverse strips or wires, Fig. B(d). If the
irises and wires are thin, they are substantially shunt reactances. If the edges of the iris
are perpendicular to the E vector, as in Fig.
8(a), the iris is capacitive; if the edges are
parallel to the E vector, as in Fig. 8(6), the
iris is inductive; in the case shown in Fig. 8(c) ,
the iris is a parallel combination of an induct-
ance and capacitance and may be designed
to be an antiresonant circuit. Thin transverse wires introduce a shunt inductance nearly
independent of the frequency. As the radius increases, the series branches of the equivalent
transducer become important.
(a)
(6)
(d)
FIG. 8
WAVE-GUIDE COMPONENTS
By George L. Ragan
12. WAVE-GUIDE CHARACTERISTICS
The form of wave guide most commonly used is a metal tube of rectangular cross-section
wfyose width a is about twice its height b. Within a twofold frequency range, only the
dominant (TEio) mode is actively propagated, and the orientation of the fields within the
tube is unique. That is, the electric field is perpendicular to the broader walls of the wave
guide. By contrast, the frequency range within which the dominant (TEn) mode in
round wave guide is propagated to the exclusion of all others is only 1.31 to lt and the
orientation of the fields within the tube is not uniquely determined by the wave-guide
geometry as it is in the case of rectangular wave guide. Consequently, bends and irregu-
larities in round tubing cause changes in field orientation and even introduce elliptical
polarization effects. It is because of this difficulty that round wave guide is little used as
a transmission line. However, round wave guide is frequently used in short sections for
rotary joints. In this application, the symmetrical TMoi mode is used.
Expressions for calculating cutoff wavelength, attenuation in copper wave guide, and
power transmitted in common wave-guide modes appear in Table 1.
Table 1. Wave-guide Expressions *
Wave-guide Shape
Mode
Xc
a/ait
P/Pit
Rectangular - -
TEio
2a
4.i6r-2- + ^Vi
6 63a6
Round
TEn
1.706d
L2S T \\J J
•5 rc f~n jon _i_ / X\ |
4.98d2
Hound
TMoi
1.306d
3.55^0.420+^ J
2.72
2.83*(^V
\\j
if X > 0.657d
* Tables and figures in articles 12-19 are reproduced by permission from G. L. Ragan, Microwave
Transmission Circuits, Vol. 9, Rad. Lab. Series, McGraw-Hill Book Co., 1948.
f a = attenuation for copper wave guide, decibels per meter. _4 2 / ,^ ^z
—
The notation used in this article is as follows:
a = larger inside dimension of rectangular wave guide, in meters.
b •==• smaller inside dimension of rectangular wave guide, in meters.
d — inside diameter of round wave guide, in meters.
X = free-space wavelength, in meters.
Xe « cutoff wavelength for the mode, in meters.
a = attenuation in decibels per meter.
P =» power transmitted, in watts.
E = electric field intensity, in volts per meter.
10-18
TRANSMISSION CIRCUITS
In Table 2, numerical values for a few representative wave guides are given. The figure
$max = 30,000 volts/ cm is based on experimental work on air at atmospheric pressure
(M.I.T. Radiation Laboratory Series, McGraw-Hill Book Co., Vol. 9, Chapter 4).
Table 2. Characteristics of Representative Wave Guides
(Courtesy McGraw-Hill Book Co.)
Army-Navy
Designation
Guide Size
CD, in.
Wall,
in.
Wave-
length,
cm
Power,*
mega-
watts
Loss.f
db/m
Copper
Wavelength J
Band, cm
A. Rectangular (TEio Mode)
RG-48/U
RG-51/U
RG-52/U. ..
3 X 1.5
1.25X 0.625
1.0 X 0.5
0.5 X 0.25
0.080
0.064
0.050
0.040
10. 0
3.2
3.2
1.25
10.5
1.77
0.99
0.223
0.0199
0.0725
0.117
0.346
7.3 -13.0
2.9 - 5.1
2.3 - 4.1
1.07- 1.9
None
B. Round (TEn Mode)
None
3 ID
I OD
10.0
3.2
16.6
1.57
0.0140
0.0847
10.0 -11.7
3.18- 3.64
None
0.032
* Calculated assuming J^max — 30,000 volts/cm.
t Calculated values for copper.
$ Based on maximum wavelength. 10 per cent below cutoff wavelength, minimum wavelength 1 per
cent above cutoff wavelength of next higher mode.
13. FLEXIBLE WAVE GUIDES AND COUPLING UNITS
Flexible wave guide is used similarly to flexible coaxial cable. Applications include
connections to shock-mounted units; connections to pieces of equipment which must be
FIQ. 1. Wound Metal-hose Wave Guide (Cour-
tesy McGraw-Hill Book Co.)
FIG. 2. Titeflex Wave Guide (Courtesy McGraw-
Hill Book Co.)
moved about; temporary or emergency replacement lines; and as patch connections,
particularly in test equipment.
Two types of construction which have proved to be especially useful are illustrated in
Figs. 1 and 2. Figure 1 shows the * 'metal-hose" type manufactured by the American
Metal Hose branch of the American Brass Co., Water bury, Conn. This type is made of
fairly heavy metal wound in the interlocking manner
indicated. Flexibility is afforded by sliding of the in-
terlocked contacting surfaces. The "Titeflex" type
shown in Fig. 2 is manufactured by Titeflex, Inc.,
Newark, N. J. Titeflex is made of thin metal wound
as shown and soft-soldered. Flexibility is afforded
by flexure of the thin metal convolutions. It has
been found that a molded-on rubber jacket affords
needed protection to both types and in addition im-
proves the performance of the metal-hose type by
causing lower contact resistance. A complete rub-
ber-covered section is shown in Fig. 3. Such wave
FIG. 3. Rubber-covered Flexible Wave- S^63 ,DMy ** beat °n radii ^ual to about 20
guide Assembly (Courtesy McGraw-Hill tHnes the respective nominal dimensions of the wave
Book Co.) guide.
WATE-GTJIDE CONNECTORS
10-19
Several other types of flexible wave guide have been found useful, especially in short
lengths, as flexible coupling units. These include: (a) Corrugated wave guide; essentially
a thin-walled metal bellows of rectangular cross-section (American Metal Hose) . The depth
of convolutions must be a small fraction of a wavelength. (6) Spun bellows assembly; a
soft-soldered assembly of thin-walled units each of which includes a circular bellows section
the depth of whose convolution is effectively one-half wavelength (American Metal Hose) .
Flexible cow
Metal hose armor
FIG. 4. Typical Vertebral Assembly; (a) is a Single Choke Disk; (fc) is the Flexible Cover; (c) is
the Assembly (Courtesy McGraw-Hill Book Co.)
(c) Cook bellows assembly (Cook Electric Co., Chicago, m.) ; a somewhat more rugged
and broader-band bellows similar in principle to (b) .
A coupling unit providing a maximum flexibility in longitudinal, transverse, and angular
displacements is the so-called vertebral type illustrated in Fig. 4. This unit is based on
the choke-flange or capacity-type wave-guide connector described in article 14 below.
Power leakage from the open space between adjacent sections is minimised by the action
of the choke grooves, and fairly large displacements may be tolerated without causing
serious impedance mismatch.
14. WAVE-GUIDE CONNECTORS
Two sections of wave guide are usually joined by couplings of either contact type,
Fig. 5, or choke-flange type, Fig. 6. The contact type has some advantages and provides
excellent results if certain precautions in design and use are observed. The choke-flange
type, however, is found to be more reliable for general use.
10-20
TKANSMISSION CIRCUITS
The design of contact couplings must be such that good contact is secured at all points
around the periphery of the butt-joined wave guides. Particular care must be exercised
to avoid the formation of cavities by permitting the contact to be made at points on the
bolting flanges before the wave-guide ends are forced into good contact. The contact
surfaces must be carefully machined and must be kept free of dirt,
corrosion, and mechanical deformations.
When these precautions are observed, a junction is obtained which
is practically perfect in all respects. This type of coupling is ex-
ceedingly valuable in certain laboratory design work where the
required care in use can be taken. Likelihood of deterioration of the
quality of the contacts in use under field conditions, however,
presents a serious obstacle to their general utility. One contact-
FIG 5 Contact Coup- tyl>e coupling which has given satisfactory service for use with 1 !/2
ling (Courtesy Me- in. by 3 in. wave guide is that designated by the Army-Navy Cable
Graw-HiU Book Co.) Coordinating Committee as UG-65/U and UG-66/U.
The choke-flange type coupling of Fig. 6, in which quality of contact is unimportant,
affords a connector admirably suited to use under adverse conditions. In addition, such a
coupling scheme is very useful in rotary joints. Parts (b) and (c) of Fig. 6 are designed
principally for such use. The wave-guide ends are slightly separated, and currents inter-
rupted by the gap A excite a folded section of line which surrounds the gap. This section
of line is terminated in a short circuit (closed end), and its length is effectively one-half
wavelength. Hence it presents at its input end essentially zero impedance to the flow
of currents interrupted by the gap A. The contact between flanges occurs at the point B,
which is at the midpoint of the half-wavelength line, and hence at a point of essentially
zero current. It is for this reason that the quality of the contact between flanges is un-
important.
Naturally, there is only one specific wavelength for which the conditions outlined above
exist, and at this wavelength only is the connector perfectly matched (i.e., reflectionless) .
In the design of such connectors, one must be guided by the principles discussed below if
a low degree of frequency sensitivity is to be achieved. Since the same principles are in-
volved in the choke-type
coupling scheme com-
monly used in most rotary
joints (see article 17 be-
low), they will be dis-
cussed in some detail.
In considering the ac-
tion of the choke-flange
coupling, it is convenient
to consider separately two
sections, each effectively
one-quarter wavelength
long at the design fre-
quency: (a) the radial sec-
tion from A to Bt and (6)
the circular groove of
depth d. The circular
groove is terminated in
zero impedance and pre-
sents at B, an effective
quarter wavelength away,
a high impedance which,
in series with the contact
resistance at Br terminates
the radial section of line.
This high-impedance ter-
mination of the radial line
is transformed to a low
impedance at A, an effec-
tive quarter wavelength away. The design problem resolves itself into that of providing,
at frequencies in the neighborhood of the design frequency, a maximum impedance at B
and a minimum impedance at A. It is easily argued that these objectives are realized
(a) by maximising the characteristic impedance of the groove section by making the
groove width x as large as is practical, and (6) by minimizing the characteristic impedance
of t&e radial Section by making the gap y as small as is practical
FIG. 6. Choke-flange Couplings; (a) Rectangular Wave Guide; (6) and
(c) Circular Wave Guide (Courtesy McGraw-Hill Book Co.)
BENDS, TWISTS, AND ANGLES
10-21
For example, let us compare the voltage standing wave ratio (VSWR} introduced to
X = 9 cm by two chokes, both perfectly matched at 10.7 cm, differing only in regard at
the values of x and y. For one design, x = 0.150 in., y = 0.104 in-., VSWR = 1.13. For
the other design, x = 0.250 in., y = 0.050 in., and VSWR = 1.03,
Design details and performance figures for a number of choke-flange units are given
in Table 3.
Table 3. Choke-coupling Design Details
(Courtesy McGraw-Hill Book Co.)
Army-Navy Type
Choke Flange
Guide
Dimen-
sions, in.
Choke Dimensions, in.
Design
Wave-
length,
cm
Band
Width for
r - 1.05,
%
H -
y \ d
a
b
Rectangular-wave-gtdde Choke.
Fig. 6 (a) — TEio Mode
UG-54/U-53/TJ ....
2.84
2.84
0.90
1.125
0.900
0.420
0.420
1.34
1.34
0.40
0.50
0.40
0.170
0.170
4.015
3.75
1. 183
1.332
1.155
0.501
0.589
0.250
0.250
0.063
0.063
0.125
0.029
0.063
0.050
0.030
0.031
0.031
O.OIO*
0.008
0.008
1.120
0.865
0.347
0.347
0.355*
0.137
0.156
10.7
9.0
3.20
3.20
3.30
1.25
1.25
±15
±15
±6
U-200/U-2 1 4/U
UG-40/U-39/U
UG-52/U-51/U
>±6
>±2
>±4
UG- 11 7 /U- 11 6/U
None
c
Circular-wave-guide Chokes. Fig. 6 (6)-— TMoi Mode
None
0.4675
1.187
0.713
1.479
0.050
0.093
0.015
0.030
0.153
0.312
1.25
3.30
>d=4
>±6
None
* Designed for 0.115-in. separation between choke and flange.
Lmearv
15. BENDS, TWISTS, AND ANGLES
If rectangular wave guide is bent or twisted gradually enough, i.e., in a length represent-
ing several wavelengths, the reflections set up in the wave guide are negligibly small. Al-
ternatively, it may be bent or twisted rather abruptly without introducing serious reflec-
tions if the mean length of bend or twist is a multiple of
half the guide wavelength. Care must always be exer-
cised to avoid the introduction of bumps or ripples in the
wave-guide walls or of excessive distortions of the cross-
sectional dimensions. The achievement of this end is
materially assisted by filling the wave guide with a low-
melting-point alloy such as Woods metal or Cerrobend
before working it, and melting it out afterwards.
Figure 7 illustrates two types of bend, designated as H-
plane and ^-plane bends, depending on whether the bend-
ing radius vector lies in the plane of the magnetic field
lines (IT) or electric field lines (JB). Incidentally, these
bends are sometimes conveniently referred to as "hard
bends" (ff) or "easy bends" (E) for obvious mechanical
reasons. The performance data for some bends and
twists are given in Table 4.
It is sometimes preferable, in order to achieve minimum
space factor, to substitute fabricated corners for bends.
Two types of well-matched corner are illustrated in Fig.
8. The double-mitered type is usually to be preferred (a)
because the dimensional tolerances are larger, and (6)
because this type can carry more power, since it has less
acute corners and a less restricted cross-section. Both
types may be designed for any desired angle, not being
restricted to the 90° type drawn.
It is found experimentally that the mean separation L
between miters in the double-mitered J?-plane corner is a
quarter guide wavelength for best match. This is easily understood as providing a cancel-
lation of mismatches by reason of quarter-wave spacing between identical reflections. In
double-mitered #-plane corners, however, the spacing deviates slightly from the expected
quarter-wave value. This is presumably because of the disturbance due to a greater
FIG. 7. Wave-guide Bends; (a)
H Bend; (b) E bend (Courtesy
McGraw-Hill Book Co.)
10-22
TRANSMISSION CIRCUITS
Table 4. Performance of Wave-guide Circular Bends and Twists
(Courtesy McGraw-Hill Book Co.)
Type
Wave-guide
Size ED, in.
Inside
Radius
Rt in.
e
Design
Wave-
length, cm
Band Width
for r below
1-05, %
E-plane bend
1.34 X 2.84
6
45°
10
>±20
1.34 X 2.84
6
90°
10
>±20
1.125 X 0.50
2
90°
3.3
± 9
0.90 X 0.40
0.50
180°
3.3
>± 9
0.90 X 0,40
0.25
90°
3.3
>± 9
0.90 X 0.40
3.00
90°
3.3
>± 9
0.420 X 0.170
0.50
90°
1.25
>± 4
fl-plane bend
1.34 X 2.84
6
45°
10
±10
1.34 X 2.84
6
90°
10
>±20
1.125X 0.50
2
90°
3.3
>± 9
0.90 X 0.40
0.192
90°
3.35
± 4
0.90 X 0.40
1.1875
90°
3.30
± 9
0.420 ±0.170
0.50
90°
1.25
>± 4
Type
Wave-guide
Size ID, in.
Length, in.
Design
Wave-
length, cm
Band Width
for r below
1.05, %
Twists
0.900 X 0.400
2
3.4
±6
0.900 X 0.400
3
3.4
±3.7
1.125X 0.500
4
3.3
>±9
0.420X 0.170
U/4
1.25
>±4
0.420X 0.170
21/2
1.25
>±4
(a)
7
$>
X
FIG. 8. Wave-guide Corners; (a) Double-mitered Type; (&) Single-miter, Cutoff Type (Courtesy
McGraw-Hill Book Co.)
excitation of local fields. Figure 9 gives the spacing found experimentally to give well-
matched double-mitered JS'-plane corners of 90° total angle. Her Xo/Xc is the ratio of
design free-space wavelength to the cutoff wavelength. The band width (for VSWH
below 1.06) is found to range from about 20 per cent (occurring for Xo/Xc of about 0.6)
to #4x)ui S per cent (for X0/X* of about 0.85).
1& IMPEDANCE MATCHING AND IMPEDANCE TRANSFORMERS
In designing a specific wave-guide component, certain parameters are varied in an at-
tempt to arrive at a design which performs its specified function and at the same time
introduces into ihe wave guide the minimum impedance discontinuity, i.e., the minimum
IMPEDANCE MATCHING, IMPEDANCE TRANSFORMERS 10-23
of reflection of the incident r-f wave. It is frequently impossible to achieve the desired
degree of freedom from reflected waves without sacrificing quality of performance in some
other respect. When such an occasion arises, it is necessary to compensate for this im-
0.31 r-
030
<0.29
0.28
027
0.50
0.60
0.70
0,80
0.90
FIF. 9 Design Curve for Double-mitered Bi-
plane Corners (Courtesy McGraw-Hill Book
Co.)
FIG. 10. Wave-guide Impedance-match-
ing Diaphragms; (a) Inductive Types; (5)
Capacitive Types (Courtesy McGraw-Hill
Book Co.)
pedance discontinuity by introducing into the wave guide an impedance-matching trans-
former.
Impedance transformers may be classified into two general categories, fixed and variable.
The fixed type is inserted at the time of
fabrication according to instructions
given by the designer, whereas the vari-
able type may be altered by the user of
the equipment to achieve the desired
performance. Though the variable
type may give superior performance
when adjusted with the required skill *
and care, it is capable of doing more K
harm than good if improperly adjusted.
The variable type is, therefore, to be
avoided whenever possible.
The fixed-type impedance trans-
former usually consists of one or more
thin metal strips soldered into the wave
guide in one of the forms shown in Fig.
10. The most widely used is the sym- FlG* •
metrical inductive diaphragm shown
in the upper right figure. The equivalent circuit and design data for this type are given in
Fig. 1 1. The asymmetrical inductive
diaphragm, design data for which are
given in Fig. 12, is used somewhat
less, as the local field distortions set
up by it are more extensive. The
capacitive types are little used be-
cause of the restriction of the per-
missible power level imposed by the
high electrical fields occurring across
the gap formed.
The curves of Figs. 11 and 12 are
for infinitely thin metal strips. A
rough compensation for increased
thickness may be made by assuming
a strip to extend into the open space
by an amount equal to half the thick-
ness of the strip.
FIG. 12. Design Curves for Asymmetrical Inductive Dia- The normalized acceptance B/Y«
phragms (Courtesy McGraw-Hill Book Co.) required to correct for a measured
10-24 TRANSMISSION CIRCUITS
voltage-standing-wave ratio r may be determined by the relation
. B r- I
(1)
Fo Vr
The distance d, from the determined position of a minimum in the voltage-standing-wave
pattern, toward the load (for inductive diaphragms) or toward the source (for capacitive
diaphragms) may be determined from the relation
d_ _ 90° - tan-^fe J3/70)
X, " 720° ^ }
Alternatively, both B/YG and d may be read from a transmission line chart or admittance
diagram.
Several other types of fixed-impedance transformer have seen limited use. One of these
is the quarter-wave transformer of ordinary transmission lines. A wave-guide section of
the desired lower characteristic impedance is formed by soldering a plate of suitable
thickness to one of the two broad walls of the guide. This plate is the full wave-guide
width and a quarter guide wavelength long. Since guide width a is not changed, charac-
teristic impedance is proportional to unfilled wave-guide height b.
Another scheme utilizes capacitive "buttons" soldered in place, or dents formed by a
suitable rounded tool. Either button or dent forms a projection from the broad wall of
the guide which acts essentially as a shunting capacitive element.
Variable-impedance transformers or "tuners" have appeared in numerous forms. They
have usually either two or three adjustable elements appropriately spaced along the guide.
Among the forms which the adjustable elements have assumed are: (a) "Stubs," or branch-
ing sections of wave guide perpendicular to the main wave guide and containing adjustable
short-circuiting plungers. The stub line may branch from either the broad wall (.EJ-plane
stub) or narrow wall (H-pl&ne stub) of the guide. (6) Screws, inserted through threaded
holes in the broad wall, (c) "Slugs," obstacles of either dielectric or metallic materials,
designed to alter the characteristic impedance of the guide in the section into which they
are inserted (usually a quarter guide wavelength long) . These slugs are ordinarily inserted
through a narrow longitudinal slot in one of the broad wave-guide walls.
Stubs may introduce either inductive or capacitive susceptance. Three stubs spaced
at quarter-wavelength intervals can, in theory, transform any load impedance into any
desired input impedance. In practice, if one is interested in matching out or introducing
a VSWR of 2 or less, two stubs spaced an odd number of eighth wavelengths apart are
adequate and have the advantage of easier adjustment.
Small-diameter screws inserted into the wave guide introduce a capacitive susceptance
only. This limitation makes the attainment of a proper adjustment much more difficult
than that for stubs. As the screw diameter is increased to a size comparable to the wave-
guide dimensions, it achieves an inductive effect when retracted, just as does a stub, which
it begins to resemble. This opens up the possibility of a screw-type tuner which is rela-
tively easily adjusted. As for stub tuners, an odd number of eighth wavelengths proves to
be a good spacing.
A single screw of small diameter, mounted on a sliding sleeve fitted closely around the
wave guide, and projecting through a longitudinal slot in the wave guide, constitutes a
very useful tuning device. By adjusting both insertion length and position along the slot,
any tuning requirement is easily met.
"Slug" tuners may be similar in action to the single screw tuner just described. Or
they may consist of two identical slugs whose overall reflection is varied by varying the
spacing between them, and the phase of this overall reflection is varied by sliding the two
slugs, as a single unit, along the guide.
A simple form of variable-impedance transformer is the phase shifter or "line stretcher"
type. This type does not alter the magnitude of the wave reflected by an impedance
discontinuity but merely alters its phase. Such a device is very useful in promoting sta-
bility of magnetron oscillators in long lines.
One common form is made simply by cutting longitudinal slots in both broad walls of
the wave guide and squeezing the section thus formed to alter the wave-guide width. As
width changes, guide wavelength aad hence total phase length of the section change.
17. TRANSITION UNITS
Whenever it is desired to couple two different wave guides together, either in the same
or different modes, some type of transition unit is needed. Similarly, a transition between
coaxial lines and wave guides is frequently needed. One very important need for transition
TRANSITION UNITS
10-25
units is in connection with rotary joints, where the dominant wave-guide mode cannot be
used (see article 18).
A number of types of transitions between coaxial lines and wave guides are illustrated
in Fig. 13. Types (e) and (/) are especially suited for low-power work; types (g), (d), and
(c) are recommended for intermediate powers;
and types (h) and (i) are especially suitable
for high powers.
A simple transformer designed to couple
from 1 by 1/2 in. wave guide to 1 1/4 by 5/8 in.
wave guide is shown in Fig. 14. Such a trans-
former section may be calculated by making
50J2 Coaxial line
X (approx,)
Probe transitions
Dimensions used
In matching
A-Iris aperture
D-End-plate distance
G-Couplfng gap
H-Contour height
.L-Loop size
P-Probe insertion
.R^lrfs position
iS-Coaxiaf stub length
FIG. 14. Quarter-wavelength Transformer be-
tween 1 x 1/2 iftch to 11/4 x 5/8 *&<& Wave Guides
(Courtesy McGraw-Hill Book Co.)
the intermediate section a quarter wavelength
long (in terms of its own \g), and choosing its
dimensions so as to give a characteristic
impedance equal to the geometric mean of
those of the joined wave guides. For this
calculation, the characteristic impedance may
be taken as
8 X0 a
(3)
If one prefers, two rectangular wave guides
could be joined by a relatively long tapered
FIG. 15. Taper from Rectangular to Round Wave
Guide (Courtesy McGraw-Hill Book Co.)
section. Such a taper is commonly used be-
tween rectangular and round wave guides, as
illustrated in Fig. 15. If space does not per-
mit such a taper between rectangular and
round guides, a transformer section such as
that shown in Fig. 16 may be used.
Transitions between the TEjo mode in rectangular wave guide and the TMoi mode in
round wave guide are particularly useful in rotary joints. Three such transition units
are shown in Figs. 17, 18, and 19. Varying degrees of complexity are illustrated. In Fig.
17, the parameters were adjusted so that satisfactory impedance match and TMoi mode
FIG. 13. Transitions from Coaxial Line to Wave
Guide (Courtesy McGraw-Hill Book Co.)
10-26
TRANSMISSION CIBCUITS
purity are obtained without the matching diaphragms or mode-filter ring shown in the
other designs. The design of Fig. IS is especially recommended for high-power work, as
no sharp corners are present to cause breakdown.
|xj*x 0.040*
rectangular
tubing •
FIG. 16. Quarter Wavelength
Transformer between Round
and Rectangular Wave Guides
(Courtesy McGraw-Hill Book
Co.)
+- 0.4675*10
round tubing
0.158*-f
FIG. 17. Transition from Rectangu-
lar TEio to Round TMoi Mode for
1.25 cm Wavelength. (Courtesy Mc-
Graw-Hill Book Co.) .
Matching windows
FIG. IS. TMoi Transition for
High-power Use (Courtesy Mc-
Graw-Hill Book Co.)
L. ^-f
Tx|' Waveguide
-^ in 2j
t
PoJyst
M*ta
xxv^a
yrene *•
1 ring "
FIG. 19. TMoi Transition with Combina-
tion Stub and Resonant Ring Filter (Cour-
tesy McGraw-Hill Book Co.)
18. MOTIONAL JOINTS
This classification includes rotary joints, oscillating joints, hinge or "knuckle" joints,
and universal joints. Rotary joints, exemplified by Figs. 20, 21, and 22, permit continued
rotation about an axis; oscillating joints oe^mit limited rotary oscillations about an axis.
Secton A-A
Rotary Joint, Combining Coaxial Line and Wave Guide, for Use at 3-cm Wavelength (Cour-
tesv McGraw-Hill "Rrw>v rv ^
MOTIONAL JOINTS
10-27
Hinge or knuckle joints, Fig. 23, permit angular displacements of one wave guide with
respect to another, the axis of the hinging being perpendicular to the wave-guide axis.
Universal joints, Fig. 24, permit the motion provided by gimbals.
Type N coaxial connector
2.840 diam.
Sern-
cylinderical'
end plate
2.56o"diarm
/
;tchlng Iris
FIG. 22. Rotary Joint Using
IG. 22. otary Jont sn
TMoi Mode in Round Wave
Guide (Courtesy McGraw-Hill
Book Co.)
Flange
Choke
Waveguide
1.340"x 2.840'
inside
dimensions
Bearing
Spring "finger"
contacts
FIG. 21. Rotary Joint for 10-cm Wavelength
(Courtesy McGraw-HIU Book Co.)
FIG. 23. Hinge or Knuckle Joints
(Courtesy McGraw-Hill Book Co.)
Any transition unit from the dominant wave-guide mode to a coaxial line or to a round
wave guide excited in a circularly symmetrical mode may serve as the basis for a rotary
joint. In Figs. 20 and 21, the actual rotation is accomplished in coaxial line. Gaps in the
coaxial line conductors are bridged by "choke couplings1' similar to those described in
article 14. A convenient feature of the high-power rotary joint of Fig. 21 is the inclusion,
within the center conductor of the main joint, of a second coaxial rotary joint for an
auxiliary transmission line.
10-28
TRANSMISSION CIRCUITS
An important consideration in the design of rotary joints using the TMoi mode is con-
cerned with the choice of a length L, Fig. 22, which avoids troublesome resonance effects.
Such resonances are associated with the dominant mode fields which inevitably exist,
despite efforts to avoid their excitation, in the round wave-guide section.
Any rotary joint may, obviously, be used as an oscillating joint merely by restricting its
rotational amplitude. A simpler design, however,
may be arrived at by applying the principles of the
vertebral assembly of chokes and flanges described
in article 13.
Two constructions of #-plane hinge joints are
illustrated in Fig. 23. Again, the choke and flange
connector is used as a basis of the design. Similar
hinge joints of $-plane type are in use.
The universal type joint of Fig. 24 is essentially
a double hinging obtained by means of gimbals and
suitable modifications of the choke-flange principle.
In this design, two chokes are opposed, rather than
choke and flange, in order to permit greater free-
dom of motion without leakage of power from the
openings around the joint. The antiresonance
plugs, shown darkened, prevent trouble from reso-
nances which are found to occur whenever two
chokes are opposed. The same resonance trouble
is found when wave guides are joined by opposing
two chokes.
19. OTHER COMPONENTS
The foregoing discussion is, of course, far from
exhaustive. Space has permitted the inclusion of
only a few designs representative of the types dis-
cussed. In addition, several types of component
have not been treated, even cursorily, because of
space limitations.
Among the more important omissions are the so-
called T-R or duplexing components which permit
the transmission of r-f power and the reception of
r-f signals on the same wave-guide and antenna
assembly. Still other circuits, which are con-
spicuously omitted, are the so-called mixer circuits
0.500*x 1.000* x 0.050*
wall brass tubing
FIG. 24.
Universal Joint (Courtesy Mc-
Graw-Hill Book Co.)
in which received signals are mixed in suitable crystals or tubes with a local oscillator
signal to generate the i-f signals supplied to the receiver.
Those interested in pursuing these omitted items will find them described in the appro-
priate volume of the M.I.T. Radiation Laboratory Series listed in the bibliography.
BIBLIOGRAPHY
1. Books of the Massachusetts Institute of Technology Radiation Laboratory Series, published by
McGraw-Hill Book CoM New York, 1947 and 1948.
(a) Vol. 9, Microwave Transmission Circuits; Ragan, editor.
(6) VoL 17, Components Handbook; Blackburn, editor.
(c) Vol. 8, Principles of Microwave Circuits; Montgomery, Dicke, and Purcell, editors.
(d) VoL 10, Waveguide Handbook; Marcuvitz, editor.
(e) Vol. 14, Microwave DupLexers; Smullin, editor.
(/) VoL 16, Microwave Mixers; Pound, editor.
(#) VoL 1, Radar Systems Engineering; Ridenour, editor.
2. Microwave Transmission Design Data, Sperry Gyroscope Co., May 1944.
3. Reference Data for Radio Engineers, Federal Telephone and .Radio Corp., Second Edition, 1946.
4. MtcroiDawe Techniques, prepared by M.I.T. .Radiation Laboratory, Bureau of Ships Publication
WAVE PROPAGATION
10-29
TRANSMISSION IN SPACE
By J. C. Schelleng
20. WAVE PROPAGATION AND GENERAL VIEW OF THE
RADIO SPECTRUM
Radio propagation is a special instance of the propagation of electromagnetic waves.
As electromagnetic waves have so much in common with light, an understanding of radio
propagation begins with an understanding of optics. Radio propagation provides ex-
amples of most optical phenomena: interference, reflection, simple refraction and double
refraction, diffraction, etc. Many of the standard formulas of optics can be carried over
without change into the radio field. Although it is beyond the scope of this article to
discuss these fundamental considerations, a few general principles will be mentioned.
RADIATION AND TRANSMISSION IN FREE SPACE. Radiation of electromagnetic
waves take place whenever an electrical charge is accelerated. The wave which is set up
is transverse, its electrical field at any point being a vector perpendicular to the direction
of transmission, lying in the plane specified by
the direction of propagation and the direction
of acceleration of charge, and measured in
units of potential per unit of length in the
direction of the field, e.g., microvolts per
meter. When the space surrounding the
source is free of material, the electrical field is
propagated outward with the velocity of
light, and at sufficiently great distances it is
proportional to that component of the accel-
eration which is parallel to the electric field at
the point in space under consideration (Fig.
1). These statements are true whether the
acceleration is sinusoidal or not. In radio
communication, the accelerated charges are
the electrons in the conductors of the an-
tenna. For engineering purposes it is more convenient to use formulas involving quan-
tities other than acceleration and charge. Thus, in free space, the electric field intensity,
E, from a short electric dipole is
Elect. Fields
Magn. Field -
DIr. of Current
and Acceleration
of Charge
FIG. 1. Vector Relations in Radiation
8 = 60x — cos 6
\d
(1)
ht d, and X are the effective height, distance from doublet to measuring point and wave-
length, all in the same unit of length (e.g., meters); 8 is in volts per unit length (e.g., per
meter), and 7 is in amperes; see article 28, pp. 5-52. A convenient form for either electric
or magnetic dipole is _ . *
- cos 9
(2)
in which P is the radiated power in watts, and 8 and d are in the same units as for eq. (1).
The field varies inversely with the distance. For an especially useful formula for the ratio
of power picked up by a receiving antenna to that radiated from a distant transmitter,
the conditions being those of free-space transmission, the reader is referred to Section 6,
article 28, eq. (11).
GROUND "WAVE AND SKY WAVE. Two general modes of wave propagation are
useful in radio communication: the ground wave, which passes along the surface of the
earth; and the sky wave, which, traveling at an angle with the surface, passes through the
lower atmosphere, is reflected from the upper atmosphere, and is enabled in this way to
return to the earth at a distant point. The ground wave is used over short distances; the
sky wave, or ionospheric wave, is required for the longer spans. Intermediate ranges may
involve either or both, depending on the frequency used, the time of day, and other
circumstances.
The reciprocity theorem of Lord Rayleigh, originally derived and widely used for
electric-circuit analysis, has been shown by Carson and others to be true in cases involving
radiation (B.S.T.J., April 1930, and earlier papers). It results from one form of this
theorem that with certain limitations the efficiency of radio transmission in opposite direc-
tions is the same, provided that the usual measures have been taken to match the generator
10-30
TRANSMISSION CIRCUITS
and load to the antennas, and that the path is free of elements which fail to act reciprocally
by themselves. A one-way amplifier is an obvious example of such an element. Another
example, less obvious, actually occurs in the upper atmosphere itself, namely, the ions
which tend to spiral about the earth's magnetic field in one direction but not in the other,
thus producing a non-reciprocal element. As a result, strict reciprocity can be expected
where the ground wave is concerned, but it becomes doubtful with the sky wave, and it
almost certainly fails where rotation of the plane of polarization (indicating a magnetic
effect) is observed. Even in the last case, the averages of field (as opposed to instantaneous
values) usually appear to be reciprocal, and this possibly is always true at the higher fre-
quencies.
POLARIZATION. For frequencies below 2000 kc vertical antennas are almost uni-
versally used. This is primarily because it is usually desirable to radiate with maximum
efficiency in a nearly horizontal direction, which is relatively easy with vertical antennas
"but is impossible with horizontal antennas unless they are several wavelengths above the
ground. Hence, to keep antenna dimensions within reasonable limits, horizontal electric
fields are not used except for short waves.
GEHERAL VIEW OF THE SPECTRUM. With respect to frequency, daylight propa-
gation falls into natural divisions. These may be listed as follows: (1) low frequency, long
THE GROUND WAVE 10-31
distances; (2) intermediate frequency, short and intermediate distances; (3) "high frequency,
all distances; (4) ultra-ionospheric frequency, short distances. Here we arbitrarily describe
a short distance as one from zero to 100 miles, an intermediate distance as one from 100 to
1000 miles, and a long distance as one greater than 1000 miles. Likewise, we usually think
of a low frequency as one less than perhaps 500 kc. Physically, the characteristic that
distinguishes a low frequency from a high frequency (3000 to 30,000 kc) is the low resis-
tivity of the reflecting layer for the low frequencies. In fact, the ionosphere resembles a
fair metallic reflector for waves of low frequencies. The wave of high frequency, on the
other hand, sees in the layers of the upper atmosphere something like a reflecting plane of
dielectric; the type of reflection which is most common is similar in many ways to the
familiar optical phenomenon of total internal reflection. The intermediate frequencies
form a transition range (500 to 3000 kc}, which includes much ground-wave transmission
over short and intermediate distances. Frequencies commonly designated as " ultra-high,"
but which are better called "ultra-ionospheric" because they are not reflected by the
ionosphere, are those greater than about 30,000 kc. At night the differences between iono-
spheric waves of different frequencies are much less marked than by day. Waves having
frequencies in excess of 1000 megacycles, more or less, are frequently called microwaves.
See also Section 1, article 24.
Figure 2 gives a typical overall view of the whole radio spectrum for distances from 100
to 10,000 miles and for vertical antennas. Lines are drawn indicating the distance at
which a radiated power of 1 kw would produce certain specified field strengths, e.g.,
1 juv per meter. Diagram a represents transmission conditions on a summer day; diagram
6, those on a winter night. On winter days, the sky wave becomes generally stronger
than on summer days. As a general rule, for a given distance the highest frequency that
can be received by day (the skip frequency) is greater in winter than in summer; and the
lowest (absorption limit) is lower in winter than in summer. At night lower frequencies
are required in winter than in summer. Transmission in the high-frequency range is
markedly affected by the changes accompanying the cycle of solar activity (e.g., sunspots) ;
since the actual phenomena are too variable to be represented by so simple a chart as
Fig. 2, the comprehensive data and predictions issued by the National Bureau of Standards
(Central Radio Propagation Laboratory) may be consulted to advantage in cases of actual
use.
21. THE GROUND WAVE
FREE-SPACE TRANSMISSION. Historically the propagation of the ground wave
has been studied by examining idealized situations. The simplest of these is the field set
up in free space by a simple doublet antenna. Equations (1) and (2) give the appropriate
solution, and apply accurately provided that the earth is known to be without effect and
the air to be a uniform and lossless dielectric. These assumptions are not true in general.
PROPAGATION OVER PERFECTLY CONDUCTING PLANE EARTH. Some situa-
tions are taken care of by assuming the earth to be a homogeneous plane and then applying
the standard principles of optics. This is particularly simple if the earth in effect has
infinite conductivity. The solution is then merely the combination of a direct wave with a
reflected wave virtually coming from the "image" of the antenna in the earth plane. With
low antennas and infinite earth conductivity we are led to a simple and important relation
pointed out at an early date by M. Abraham. For distances short enough not to violate
the assumptions as to the effective flatness of the earth and negligible attenuation, a short
vertical grounded antenna of effective height h produces a field strength 80 is- the region
about it equal to
80 = 1207T ^ cos 0 (3)
a\
units as in (1). The formula corresponding to (2) is
V9OP _ ,,_
80 = ; COS 8 (4)
a
The doubling of the numerical factor in passing from (1) to (3) merely expresses the fact
that the field may be regarded as the sum of one field received directly and another by
reflection from the image. Note, however, that (2) and (4) being expressed in terms of
power instead of current have factors in the ratio of 1 to -v/2. Formulas (1) to (4) apply
for distances greater than a few wavelengths. When the distance is of the order of 1
wavelength or less, the term due to acceleration of charge is supplemented by terms due to
velocity and position (proximity) of charge, but for most practical purposes these may be
neglected for distances greater than 1 wavelength. Except in the immediate vicinity of
10-32 TRANSMISSION CIRCUITS
the antenna, the velocity of phase propagation is 2.998 - 1010 cm per sec, the velocity of
light in air.
PROPAGATION ALONG A PERFECTLY CONDUCTING SPHERICAL EARTH. A
next step beyond that represented by (4) is the propagation of a field from a vertical
grounded antenna, located at the surface of a perfectly conducting earth which is spherical
rather than plane. Watson's solution [Proc. Roy. Soc. (A) Vol. 95, S3, 546 (1919)] is in
the form of a series in which all but one term may be neglected at the greater distances.
This term is as follows:
J4
& = 0.11368o ~^ e-°-oo376d/xH (5)
where CQ is the inverse distance field as given by (3) or (4), and d and X are in kilometers, d
being measured along the surface. This formula holds when d/\™ > 160. For smaller
distances, (3) or (4) applies. In (5) , atmospheric refraction has been neglected.
The following simple empirical formula based on Watson's results and on calculations
of other terms in his series carried out by C. R. Burrows can be used for distances less than
about 5000 km: . .
8 = 8o(l + 2s)^e-' (6)
where z = 0.0035 d/\^ and d and X are in kilometers. All these diffraction calculations
assume that the density of the lower atmosphere is independent of height; atmospheric
refraction is neglected. When the deviation of refractive index from that at ground level
is a simple linear function of height, refraction has the same effect as increasing the size
of the earth to a virtual radius which for average conditions is about 4/s the actual radius.
With refraction we have z — 0.0029<i/X^- It is not obvious which of these values should
be used. Although the refraction effect is important at sea level, it must become small at
heights of several miles. Perhaps the effect can be neglected at low frequencies. At higher
frequencies experiments clearly show that it should be taken into account.
TRANSMISSION ALONG AN IMPERFECTLY CONDUCTING PLANE EARTH. At
distances shorter than those which give appreciable attenuation due to the shadow of the
bulge of the earth, strong attenuation due to energy dissipation in the ground is found in
many cases of importance in practice. Since the shadow effect is then unimportant, the
solution of wave propagation over a plane of finite conductivity becomes applicable. The
basic solution of this problem, due to A. Sommerfeld [Ann. der Physik, (4) Vol. 28, 665
(19O9)3, has been extended by various investigators. Owing to finite earth conductivity
the wave ceases to have the simple form contemplated in connection with eq. (3) for infinite
conductivity, the inverse-distance attenuation of which represents a spherically expanding
wave. The field strength at the surface decreases in intensity more rapidly than the
inverse of distance, owing to the absorption of energy by the currents set up in the im-
perfectly conducting earth. For the lower frequencies, an approximation due to van der
Pol {Jahrbuch der Drahtloson, Vol. 37, No. 4, 152 (1931)] is useful. This is:
o (2 + 0.3p)
'
where €Q is the inverse-distance field given by (3) or (4) and
T - 10~18 d
P = ~~6~ ' M
tr is the conductivity in emu units and varies from 1 to 4 X 10 ~u for sea water to 10 ~15 for
very broken land; d and X are expressed in kilometers; p is the "numerical distance" of
Sommerfeld. Note that according to (7) the field varies inversely as the first power of
distance near the transmitter and inversely as the square of the distance for p ^> 20. Also
note that, since X and cr enter only as the product <rX2, the field strength remains unaltered
when the wavelength is decreased by a factor, provided that the conductivity is simulta-
neously increased by the square of that factor. Equation (7) holds only so long as the di-
electric currents in the earth remain negligible compared with the conduction currents.
This is insured if the frequency in kilocycles is very low compared with 1.8 X 10 ~l* tr/K, K
being the dielectric constant of the ground. Numerically, the frequency should be con-
siderably lower, for sea water, than 106 kc; for land, than 104 kc; and for fresh water, than
250 kc, the figure depending on the ground constants, which differ from place to place and
to some extent with temperature.
An interesting characteristic of waves traveling along an imperfect conductor, first dis-
cussed by J. Zenneck [Ann. der Physik, (4) Vol. 23, 846 (1907)], is that parallel to the sur-
face there is a longitudinal component of electric field, that is, one extending in the direction
THE GROUND WAVE
10-33
of propagation. Its amplitude and phase depend on the resistivity and dielectric constant
of the ground, the phenomenon being very different over fresh water, sea water, moist
ground, and dry ground. Its
amplitude is zero for perfect
conductivity and increases as
the conductivity decreases.
The phase of this component
in general differs from that of
the vertical component so
that in the vertical plane the
wave exhibits elliptical polari-
zation. By Poynting's the-
orem the existence of this
component is a necessary ac-
companiment of energy loss
in the ground. The phenom-
enon is of importance in the
design of wave antennas,
which depend for their effec-
tiveness entirely on this hori-
zontal component. [See
"Wireless Waves at the
Earth's Surface" by G. W. O.
Howe, Wireless Engineer, VoL
17, 385 (September 1940).]
IMPERFECTLY CON-
DUCTING SPHERE. A still
closer approximation to ac-
tual conditions is afforded by
the assumptions that geomet-
rically the earth is a perfect
sphere (i.e., that local irregu-
larities may be ignored) and J
that electrically over any
given path it has uniform con-
ductivity and specific induc-
tive capacity. As to refrac-
tion in the atmosphere, the
assumption made above in
connection with a perfectly
conducting sphere is repeated.
Though these assumptions
still describe a somewhat ide-
alized picture, they neverthe-
less represent a large step in
the direction of realism, a dif-
ficult and important mathe-
matical task which has been
successfully accomplished by
the combined labors of several
investigators, including Balth
van der Pol. Excellent sum-
maries, including bibliogra-
phies, have been given by C«
R. Burrows and M. C. Gray
[Proc. I.RJE., Vol. 29, No. 1,
16 (January 1941)] and by K
A. Norton [Proc. I.R.E., Vol.
29, No. 12, 623 (December
1941)]. Figures 3, 4, and 5
are based on the paper of
Burrows and Gray.
Figure 3 gives theoretical
field strengths between two
100
80
60
40
20
0
-20
-40
100
80
0
| 60
>
2-40
1 20
1
0 0
a
-20
^
^*s^
1
I
\
^
>i^>
^x""
xX
Freq
me
uen
lac*
cy In
cles
1
Vertlca |
polarization
Poor soil
x
X
x
*s
>>Hx
^
x£
X
x
s
-IX
X
X
x
>J_V_
X
"X
\
X
x
N
s f ^S
k N
\
X
x
K
N:^\
N
\
\
\
\60 '
v!iX
^\
\
^
s
\
,600 \
\l <
\
\
\
\
\
""•*»,
^x^
^
\
"^
x
•*4,
N5^^fc^
Vertical
polarization
Good soil
x
x
x
x.
X
X
Sk;
X
x
x
X
x
s s
|bx
x
2
\
x
X
Tx
x
x
\
S
"S
0.
\
6 \
^
I "^
X
\f
\
\
\
\
\
\€
• \
\
y
\
60CJ
\\
\
\
\1\
\ i
\
100
80
60
40
20
0
20
-40
0
""^x
^^
^
^L"**
--,.
X
Tt^.
Vertical
polar zatlon
Sea water
X
s,
•«,
-<5:
rk
x
X
X
\
^
^
X^-2
(
x
N
\
\
^
\:
.5\^
\
f
\S
\
N600
\
\
\
\
1
\
512 5
10 20 &0
Distance In miles
100 200 500 1000
FIG. 3. Field Along Imperfectly Conducting Spherical Earth, with
4/3 Earth-radius. Short vertical antenna at ground level, measure-
ment at ground level, for sea-water <r = 4: X 10"11 emu, € = 80;
good soil or = 2 X 10 ~13 emu, « = 30; poor soil <r = 10 ~14 emu,
e = 4, 1 kw radiated (Courtesy Proc. I.R.E.)
points on the surface of the earth when vertical polarization is used. "Standard refraction"
10-34
TRANSMISSION CIRCUITS
conditions (4/3 earth radius) are assumed to occur over a sufficient depth, of atmosphere to
produce bending at all
100 | — *=vT — 1 Mini ! ! mn 1 I .^I.l.U'n frequencies, a postulate
frequently made which
might, however, prop-
erly be questioned with
reference to the lower
frequencies shown, since
with them transmission
to the longer distances
involves at intermediate
points regions which are
far above the earth's
surface and at which the
rate of decrease of re-
fractive index with
height is no longer com-
parable with that at the
surface. The legend of
the figure gives the soil
constants assumed in
the calculation. Impor-
tant features of the
curve are the "inverse-
distance" tendency at
the upper left corners as
in the approximation of
eq. (4), the rapid drop
due to failing diffraction
at the lower right as sug-
gested by eq. (5), and
the inverse square of
distance in between as
indicated by eq. (7) (for
-20
Distance in mifes
100
1000
Height sain In decibels
H* M w
o o o o
^
-
^
^
^
^
15(
\ M
c
— -
— -
,— -
,^-"
> 10 20 30 50 100 20
Antenna heighi to feet
FIG. 4. Fields at 150 Me as a Function of Height of Transmitter and
Receiver, Good Soil (Courtesy Proc. I.R.E.)
100
-20
foorjsoH-
5ea Water
10
I polarization
' -Poor soil I
•Good soil]
•Sea water
p }§> 20). A useful series of calculations along these general lines (K. A. Norton) is included
in "Standards of Good Engineering Practice Concerning Standard Broadcast Stations/'
issued by the Federal Communi-
cations Commission, for sale by
the Superintendent of Docu-
ments, Washington 25, D. C.
This document also gives com-
prehensive information of the
ground conductivities pertinent
in this frequency range in the
form of a United States map.
Figure 4 illustrates propaga-
tion from one point on or near the
ground to another at heights from
zero to 40,000 ft above it for the
special case of 150 megacycles.
If the transmitting antenna (ver-
tical polarization) is on the
ground, the upper graph gives the
calculated field directly. The
lower graph gives the correction
to be added if the antenna is ele-
vated not more than 200 ft. The
increase which accompanies the
elevation of the receiver, and the
inevitable failure of diffraction at
50
Distance In miles
greater distances, are striking
features of the graph.
Figure 5 exemplifies for fixed
antenna heights and fixed fre-
<atteucy how the field depends on the underlying ground and on the polarization. Note the
eness of horizontal polarization to ground constants.
FIG. 5. Fields at 150 Me and 10,000 Ft. as a Function of
Ground and Polarization (Courtesy Proc. I.R.E.)
THE GROUND WAVE 10-35
ULTRA-IONOSPHERIC RANGE. This is the range of frequencies higher than those
capable of reflection by the ionized upper atmosphere. The dividing frequency is not at
all sharp or constant but is of the order of 30 megacycles. Ultra-ionospheric waves whose
length is short enough for the practical application of quasi-optical techniques such as the
use of parabolic reflectors and lenses have been called "microwaves," and here an equally
hazy division might be placed somewhere near 1000 megacycles.
Although the absence of reflection of ultra-ionospheric waves might hypothetically be
accounted for by their penetration into a region where they are dissipated by absorption
before being freed by reflection, three experiments now indicate actual passage through
the ionosphere into interstellar space. In chronological order these are the detection of
galactic noise by K. Jansky (and the subsequent mapping of the Milky Way by Grote
Reber), the measurement of thermal radiation from the sun by G. C. Southworth
[J. Franklin Inst., Vol. 239, No. 4, 285 (April 1945)], and the dramatic "detection and
ranging" of the moon by radar reported by DeWitt et al. [J. Mofenson, "Radar Echoes
from the Moon," Electronics, Vol. 19, No. 4, 92-98 (April 1946)]. These experiments
strongly suggest inadequacy of ionization as the reason for absence of reflections.
Qualitatively propagation in this range strikingly resembles the familiar phenomena of
light. Radio "vision" tends to be limited to the optical line of sight, though diffraction
actually extends coverage considerably beyond obstructions, such as hills or the bulge of
the earth, except for extremely high radio frequencies. The earth (land or water) for many
purposes may be regarded as an example of Lloyd's mirror, the ground-located receiver
tending to be in the first dark fringe produced by reflection. Refraction tends to make the
distant station "visible," just as it reveals the sun a few minutes before sunrise, and it pro-
duces variations and anomalies which correspond to the twinkling of stars and to the
mirage. The comparison might be extended to other phenomena.
The effect of regular reflection is most pronounced in the meter range, though even in
the centimeter range cleared land or water may make a good "mirror" for glancing inci-
dence. In such cases reflection may be calculated as to amplitude and phase by means of
standard optical formulas provided that an equivalent conductivity and dielectric constant
are known. [P. O. Pederson, The Propagation of Radio Waves, Copenhagen, 1927; C. B.
Feldman, "The Optical Behavior of the Ground for Short Radio Waves," Proc. I.R.E.,
Vol. 21, No. 6, 764 (June 1933); Barfield, J. IJ8.E., Vol. 75, No. 452, 214 (1934); R. L.
Smith-Rose, J. I.E.E., Vol. 75, No. 452, 221 (1934).] As has already been implied, though
reflection has a favorable effect with long waves of vertical polarization, causing the factor
of 2 which differentiates eq. (3) from (1), in this range it is commonly unfavorable owing
to the phase of the reflection coefficient caused by the predominance of dielectric currents
in the ground at these ultra-high frequencies. The effect of reflection need not be unfavor-
able, however, if one or both of the terminals is located at a sufficient altitude. At high
enough altitudes a regular succession of maxima and minima is encountered, whose posi-
tion and amplitudes may be calculated from the amplitude and phase of reflection.
In the microwave range caution is necessary in applying the concept of reflection. Here
one may not always regard the earth as the smooth and abrupt boundary between materials
described simply by their conductivities and specific inductive capacities. Reflection is
not always specular but is very likely to be diffuse, as the success of radar mapping proves.
One should not ignore even here, however, the strong tendency toward specular reflection
that glancing incidence imparts to the scattering from a rough surface.
Simple plane-wave reflection theory leads to a useful relationship which has been ob-
served to hold with fair consistency in the range from 3 to 10 meters and even in the
microwave region if the warning in the last paragraph does not apply. Over level land or
over fresh water with vertical or horizontal antennas, and over sea water with horizontal
antennas, the received field is:
8 = 12ir V5 volts per meter (8)
or X
the radiated power P being in watts, and d, H\, Hi, and X in meters. HI and HZ are altitudes
above the general reflecting area, be it ocean, valley floor, or plain. This equation is
obtained by multiplying the free-space field of eq. (2) by ^irHiHz/hd, a procedure justified
if HiH»_/\d is less than 0.1 provided that the reflecting coefficient of the ground is near
unity for the grazing incidence involved. The usefulness of eq. (8) is not limited to trans-
mission over plane earth, as assumed in its derivation, but roughly applies also over
spherical earth for transmission below the line of slight when 3 meters < X < 10 meters,
3 meters < H < 25 meters, 1 km < d < 50 km. In this extended range (B) is to be
regarded as an empirical formula whose range of validity has not yet been determined.
When terminals are located on hills, with a level valley between, this formula needs a
correction factor due to ground reflections local to the terminals.
10-36 TRANSMISSION cmCTJITS
An interesting extension of eq. (8), valid within the same limitations, is obtained
analogously to eq. (13) in the section on radio antennas. If GT and GR are the power gains
of the antennas (in terms of an "isotropic radiator"), and PT and PR the powers trans-
mitted and received, it can be shown that
Note that power received is independent of frequency. If the antennas are short doublets,
G = 1.5. (K. Bullington, Proc. I.R.E., 1947.)
With vertical antennas over sea water, but otherwise with conditions specified above,
an approximate inverse-square-of-distance variation has been found up to 30 or 40 km,
with the important difference that propagation became poorer as the frequency was raised.
This is in accord with simple optical theory, due account being taken of the electrical
constants of sea water. Equation (8) therefore does not apply here, though it does for
horizontal antennas over sea water.
Since diffraction extends the range beyond obstacles it is a favorable factor. Ignoring
diffraction and refraction we could at most transmit only_to points above the line of sight.
The range would then be limited to D = 3500(V#i + Vjffa), all distances being in meters.
Within this range eq. (8) is applicable unless the antennas are too high, with qualifications
already mentioned. Note that line of sight does not at all guarantee the free-space field
strength.
It is possible to make instructive calculations of the fields behind obstructions, such as
hills, by application of the standard mathematical theory of diffraction. Thus, the be-
havior of a knife edge in the familiar optical example becomes a guide in radio transmission
past obstacles. In a radio problem, in order to obtain a reasonable estimate of this kind,
the effect of ground reflection at the transmitter and at the receiver needs to be taken into
account.
If the index of refraction of air is calculated as a function of height from average meteor-
ological conditions [Humphreys, Physics of the Air, McGraw-Hill (1940), p. 80], the gradual
decrease of index leads to a "standard" or "normal" condition which can be taken into
account in a simple manner. Such calculations and theoretical considerations indicate
that, if the topographic cross-section of the path is plotted as though the earth had a
radius 4/3 times its actual radius, the solution of the corresponding problem assuming a
uniform refractive index is also the solution for the actual problem including the effect of
refraction. We have already had occasion to use this method above in the "spherical
earth" problem. In dealing with microwaves, however, this simplication will be misleading
if the possibility of many other distributions of refractive index is forgotten.
In connection with the foregoing topics, reference may be made to articles in Proc. I.R.E.,
Vol. 21, No. 3 (March 1933), by Jones (p. 349); Trevor and Carter (p. 387); Schelleng,
Burrows, and Ferrell (p. 427) ; and Englund, Crawford, and Mumford (p. 464) ; also Eng-
hind, Crawford, and Mumford, B.S.T.J., Vol. 14, No. 3, 369 (July 1935).
At shorter wavelengths refractive variations within a small range of height may become
important because the wave in traveling between two points occupies only a small fraction
of a kilometer (that is, the necessary Fresnel zones are now included in a small transverse
area). It results, for example, that such waves may be trapped beneath a level of minimum
refractive index and may travel unusually long distances, and that under other conditions
they may unexpectedly fail over short ones.
Refraction theory as applied to extremely short waves has led to the use of a modified
refractive index of the air, M, as a function of height, h. If the actual index as ordinarily
used is n(h] and the radius of the earth is a, the definition M - 10 ~* = n(h) — 1 + h/a
leads to the same solution with an assumed fiat earth that the actual index leads to with
curved earth, the scale factor 10""6 being used for numerical convenience.
Just as short waves are "bent down" by the ionosphere because its refractive index
decreases with height — that is, the phase velocity increases with height — so in the tropo-
sphere a decrease in modified index will tend to confine microwaves beneath it. Indeed,
if meteorological conditions are such as to give a maximum index at a certain level with
progressively smaller values above and below, one would on ray theory expect the ray in
its horizontal passage to undergo consecutive upward and downward bendings about the
level of maximum index (minimum velocity) . Similarly the wave might be confined be-
tween an index which decreases with height and the reflecting floor of the ocean (or perhaps
of land). Such phenomena do occur, and their importance is that they may lead to ab-
normally high or abnormally low fields. The reason for the strong fields is that cylindrical
rather than spherical expansion causes a slower decrease with distance, i.e., increased
range horizontally. The phenomena resulting are likely to be complicated and variable,
though on the other hand such "anomalies" may be so consistent as to be the normal
THE SKY WAVE 10-37
condition. ["9 cm and 3 cm Propagation in Low Ocean Ducts" by M. Katzin, R. W.
Bauchman, and Wm. Binnian, Dept. of Com., Office of the Publication Board, Report
PB 13747 (1945) ; "Wave Theoretical Interpretation of Propagation in Low Level Ocean
Ducts'* by C. L. Pekeris, Dept. of Com., Office of the Publication Board, Report PB
20228.] Another way of looking at these ducts is to use wave guide concepts: in fact, a
duct is a wave guide with many modes of propagation which are excited to different extents
depending on the elevation of the transmitter with reference to that of the duct. The
second article cited discusses the subject from that point of view. For a summary of the
war work dealing with the various aspects of this problem see Radio Wave Propagation,
Consolidated Summary Technical Report of the Committee on Propagation, by Burrows and
Attwood, Academic Press, New York.
With wavelengths longer than 10 cm the absorption of energy from the wave due to
the atmosphere itself is not important for practical purposes, but with shorter waves at
least three known mechanisms may have to be considered. Water in the liquid or solid
phase (e.g., rainfall) is one of these that can become very serious at wavelengths of a
centimeter or two. The loss depends on the total water per unit volume and on the size
of drop or particle and is due to scattering. Although this is harmful to radio transmission,
the phenomenon is being utilized by meteorologists in the detection and location of storm
areas by means of radar. In the vapor phase, water has its longest wave resonance at 1.3
cm, so that near this wavelength high absorption is to be expected and is found for high
humidities. Oxygen has its first resonance absorption at 0.5 cm.
Directional properties of tropospheric waves have been studied at a wavelength 3.25
cm by W. M. Sharpless, and at 1.25 cm by A. B. Crawford and W, M. Sharpless, Proc.
I.R.E., Vol. 34, No. 11, 837-848. Deviations in azimuth were found to be at most of the
order of 0.1°. Although in elevation the deviations were several times as great as this,
they were never large. Fading about the free-space field strength was observed, and at
times the field exceeded this by a factor of 4 (12 db). At times there were multiple waves
coming in from slightly different directions, the variations of which produced fading.
22. THE SKY WAVE
THE IONOSPHERE. Whereas for most radio services up to a few hundred miles
transmission depends on the direct ground wave, for all long distances successful transmis-
sion depends on the existence of a "ceiling" in the upper atmosphere which, by returning
to the earth the outgoing waves, lays down a useful signal at distant points where the
ground wave is negligible. Even the longest waves used in radio communication depend
on such "sky waves" for distances beyond a thousand miles or two. In this section we
shall describe present views of this ceiling, the common name for which is the "ionosphere,"
formerly called the "Kennelly-Heaviside layer." The first suggestion that an electrically
conducting region exists in the upper atmosphere was made by Balfour Stewart to explain
variations in the magnetic field of the earth. Kennelly and Heaviside were the first to
see the necessity of such a region for explaining radio transmission phenomena.
At sea level, the atmosphere is scarcely conducting at all, but as the elevation is in-
creased the conductivity increases owing to an increase in the number of ions in unit
volume. This ionic density increases both because the major sources of ionization are
outside the earth and because, at the lower pressures encountered, the ions last longer
before recombination neutralizes them electrically. Heavy ions (e.g., ionized molecules)
have much less effect on radio waves than electrons. Electrons are known to exist in
sufficient quantity in the upper atmosphere to produce most of the effect observed, but
the radio effects of heavy ions have not as yet been definitely identified. The number and
distribution of these ions depend on various factors, including altitude, geographical and
geomagnetic latitude, local time, time of year, and solar activity (e.g., sunspots) . The varia-
tion with altitude is very important. It has been found that the increase with altitude is
not at all uniform and simple, but that there are regions where the density attains, or
tends to attain, maximum values. Although methods thus far devised are not suited for
studying those levels above the maxima where (the density may actually decrease with
height, it is probable that one or more of such decreases actually occur. These levels of
mn.TriTm.im (or tendencies thereto), frequently called "layers," are illustrated in Fig. 6.
The maximum occurring somewhat above 100 km is known as the E layer, and those
above 160 km as the F layers, names which will perhaps be superseded when the mecha-
nism of their production is explained. It is fairly definitely known that ultraviolet light
from the sun is an important source of ionization, particularly in the E region and in one
region of the F layer. This leads to the large differences between the day and night
behavior of radio waves, in particular to phenomena occurring at sunrise and sunset.
10-38
TRANSMISSION CIRCUITS
400
Another cause of ionization is particles from the sun, which most authorities regard as
the radiation by which solar disturbances communicate the major disturbing effects to the
earth. These are in particular thought to be the cause of the absorbing "clouds" which
seem to form in polar regions beneath the E layer and hinder short-wave transmission
during magnetic storms. The distribution of ionization changes with time, and Fig. 6 is
to be regarded merely as typical. Tendencies toward maxima come and go, and both
the E and F regions seem to be composites of two or more layers. The E layer is the most
consistent and is the most important one in the broadcast band (1500 kc and lower) and
at lower frequencies. For
50Oj 1 -j these lower frequencies, the
waves do not ordinarily pene-
trate higher than the E layer.
For the lowest frequencies it is
not known whether reflection
occurs at the E layer or at
some lower level, there being
some evidence that the height
is 80 or 90 km. The F region
is of most importance for the
short waves, particularly over
longer distances, but the E
region also contributes com-
ponents to the signal, which is
usually very complex.
The most fruitful method
of studying these regions has
E300
~2QQf-
100
""«O
F Reglon
-E Region-
Noon
10°
O 0 5xl06
Electrons per Cubic Centimeter
3?iG. 6. Concentration of Electrons in the Upper Atmosphere, been the pulse or echo method
The D region b the ionosphere below &0 km, the F region is the of Breit and Tuve [Phys. Rev.,
part above 160 km, and the E region, is the part between, these ,._.._ V 1 98 554 CloW^I "
which a very short-wave train
of a given frequency is radiated upwards and the times required for various reflections to
be returned are obtained with an oscillograph, preferably of the cathode-ray type. These
times may be converted into virtual heights of the reflecting layer by assuming the pulse
to travel with the velocity of light. This method of "radio detection and ranging" is in
fact one of the forerunners of radar. Actually, the pulse travels with a slower group
velocity than this while in the ionized region, but as a result of making measurements at
several frequencies it is often found that the virtual height within limits is nearly independ-
ent of frequency, and for such frequencies the actual cannot be very different from the
virtual height. Transmission through the ionized region is complicated by the earth's
magnetic field, which makes of it a doubly refracting medium in which the wave is broken
into two components of different polarization traveling with different velocities. It is
this characteristic which has led to the identification of the electron as the active ion. The
magnetic field leads to complications in practical communication by causing rotations in
the plane of polarization, leading to one type of fading (see later section on fading) and to
errors in direction finding with loop aerials.
It is natural to suppose that the electrical characteristics of the ionized region are linear,
so that different disturbances may be superposed without interaction.. Evidence has
been found, however, that this is not invariably true [B. D. H. Tellegen, Nature, p. 840
(June 10, 1933)3- If two broadcasting stations of high power operate on entirely different
wavelengths and are separated by some hundred kilometers, modulation originally im-
pressed on one has been found under certain conditions to have been transferred to the
wave of the second. This indicates that the ionosphere does not have strictly linear char-
acteristics. It is called the Luxemburg effect.
For detailed information on the ionosphere, and for bibliographic references, the follow-
ing may be of interest: E. V. Applet on, Inst. E.E. (London}, Vol. 7 (September 1932);
Kirby, Berkner, and Stuart, Proc. I.R.E., Vol. 22, No. 4, 481 (April 1934) ; Schafer and
Goodall, Nature, June 3 and Sept. 30, 1933; Bellinger, Trans. A.I.E.E., Supplement,
Vol. 58, SOS (1939); Darrow, Bell Sys. Tech. J., Vol. 19, No. 3, 455 (July 1940).
^ SKY-WAVE PROPAGATION. It is the general belief that waves which travel long
distances do so by means of multiple reflections, although tbe suggestion has been made
that short waves (e.g., frequencies above 3000 kc) do so in a single step. Thus, in Fig. 7
a wave is conceived to travel from A to B by three reflections from the E region (3), or
by fcwo from the F region (2). The single-step path is represented by curve 1. If at each
ioaospfeerie reflection double refraction due to the earth's magnetic field were to occur,
for tibe two-reieetion wave not one but four (22) components might be found, and for the
THE SKY WAVE
10-39
three-reflection mechanism, eight. Whether the complexity is thus explained or not, it is
a fact that the received wave is frequently very complicated. As Fig. 7 suggests, there is
wide diversity among components in their angles of elevation. In general, however, for
all these paths, the received energy arrives with a downward component of velocity. This
is of great importance in practice, since the mode of transmission places important direc-
tional requirements on the antennas at the two terminals. In the horizontal plane, radio
waves as a general thing travel along the great circle denned by the locations of the
terminals. Consequently, the waves on arrival are usually directed approximately along
FIG. 7. Sky-wave Propagation according to the Ray Theory
the true bearing of the transmitter, regardless of frequency range. Small variations and
differences exist in azimuth, with occasional large ones. See Friis, Feldman, and Sharpless,
Proc. I.R.E., Vol. 22, No. 1, 47 (January 1934); Friis and Feldman, Proc. I.R.E., Vol. 25,
No. 7,841 (July 1937).
LOW FREQUENCIES (LONG "WAVES). Among the chief characteristics here are:
(1) at a given frequency, the diurnal variation of the field and the difference between day
and night attenuation; (2) by day, the greater attenuation at the higher frequencies; (3)
by night, the relatively low attenuation and the relative independence of attenuation on
frequency; (4) seasonal variations; (5) propagation substantially along the great-circle
path and the departure and arrival in a substantially horizontal direction; and (6) the
practical absence of fading.
Typical diurnal variations of field strength from American transatlantic long-wave
stations as received in England are shown in Fig. 8, which is reproduced from Espensehied,
Anderson, and Bailey, Proc. I.R.E., Vol. 14,
No. 1, 7 (February 1926). The times when
the path is entirely in daylight, entirely in
darkness, and partially in each are shown by
the shading in the strip at the bottom.
Both seasonal variations and diurnal varia-
tions are brought about by the changing posi-
tion of the path relative to the hemisphere
illuminated by the sun. In the summer, the
duration of the daylight transmission phe-
nomena is naturally longer than in the winter
on account of the longer days. It is this
change in the lengths of the day and night
periods which is the most striking feature of
the seasonal variation, rather than any
change in the strength of signal. When the
entire path is illuminated by the sun, or when
the entire path is in darkness, the character-
istic day or night phenomena are observed.
When the path is half illuminated, half dark-
ened, a characteristic minimum may be found
in the diurnal curve. This is illustrated in
Fig. 8, which shows a pronounced minimum
occurring near sunset in the 57,000-cycle curve.
It is evident that the field to be obtained at
any time cannot be predicted by any simple
formula, but if precision is not required it is possible to determine its order of magnitude
for the night and for the day condition. Very roughly, the midnight field in long-distance
transmission has an average of the order one-fifth the inverse-distance value. By day,
the fields are more consistent and the average values are indicated by the Austin-Cohen
formula,
G.M.T. 12
10 12
7 9 11
135
A.M.
E.S.T. 7 9 1"! 1 3 5
P.M.
8. Diurnal Characteristics of Low Fre-
quencies in Transatlantic Propagation
FIG.
sin u
10-40
TEANSMISSION CIRCUITS
where So is given by (3) or (4), # in radians is the angle subtended at the center of earth
by the path D is in kilometers, and /is in kilocycles and is less than 1000 kc. These con-
stants were suggested by Austin in 1926 [Proc. I.R.E., Vol. 14, No. 3, 377 (June 1926)] in
order to make the formula more nearly universal for daytime transmission than the original
formula, in which the exponent was -87 X lO^-D/0-5 A convenient form is
10*
(10)
in which P is radiated power in kilowatts and E is in microvolts per meter. The difficulty
of expressing transmission data in this simple and usable form is brought out by the fact
that in one part of the frequency range covered, namely from 17 to 60 kc, data received
in transatlantic transmission are better represented when the exponential factor is modified
to s-4 x iQ-W1'88 [Espenschied, Anderson, and Bailey, Proc. I.R.E., Vol. 14, No. 1, 7 (Feb-
ruary 1926)].
Effects accompanying magnetic storms, and secular variation, are discussed under
"Solar Disturbances" in article 23.
INTERMEDIATE FREQUENCY. As indicated in Fig. 2, the daytime field of the
sky wave in this range, broadly speaking, is attenuated beyond the possibility of usefulness.
Apparently enough ultra-
violet light from the sun
penetrates to levels of the
order of 100 km to maintain
an absorbing stratum of
ionization in spite of rela-
tively rapid recombination.
Near sunset, however, this
cloud disappears, permit-
ting a considerable reflection
to distant points on the
ground during the night.
There is still absorption,
and it is variable as Fig. 9
shows, but propagation to
long distances is ordinarily
possible. (See Standards of
Good Engineering Practice,
loc. cit., from which Fig. 9 is
reproduced.) Note that
~2000 2400 2800 this figure is reasonably con-
sistent with the value one-
fifth of inverse-distance field
mentioned in the preceding
section for low frequencies.
AveUge Uy wave field
(corresponding to be sfecond
hodr after sunset at th
•recordfng sta.ion/
0.0002
OjDQOl
FIG. 9.
400
800
12OO 1500
Miles
Night-time Field Strengths from 250 to 2700 Mfles (F.C.C.
Data)
To a first approximation night-time transmission in this range is independent of fre-
quency.
HIGH FREQUENCIES (SHORT WAVES). In contrast with the low-frequency range
discussed above, there is a range of frequencies above approximately 3000 kc m which
daylight sky wave transmission improves with increasing frequency, though this trend is
subsequently reversed. This short-wave range is limited at the high-frequency end by
the inadequacy of electrons per unit volume of the ionosphere. The limiting frequency
in the daytime is not very different from 30,000 kc (10 meters). Both limits are variable,
and the figures given are somewhat arbitrary. Among the chief characteristics of trans-
mission in this range are: (1) the diurnal variation of field strength and the prominence of
day-to-day fluctuations; (2) the greater distances of transmission obtained with the higher
frequencies, especially by day; (3) the "skip" effect, or the existence of a region about the
transmitter in whiefe the direct wave is absent owing to attenuation of the ground wave,
and the sky wave, if present at ail, is weak and erratic owing to electron limitation; (4)
habitual fading, sometimes of extreme rapidity, and the common occurrence of selective
fading; (5) the necessity in most cases for more than one frequency for 24-hour service;
(6) the great reduction of field strength in northern and southern latitudes concomitant
wilfo magnetic storms and, by contrast, the absence of a pronounced effect in equatorial
regions, and other phenomena having a solar origin; (7) a secular variation following the
11-year sunspot cycle; (S) great-circle transmission and a wide variety of angles in the
vertical plane.
THE SKY WAVE
10-41
Diurnal Variation. Typical diurnal variations are shown in Fig. 10, which depicts the
changes occurring in a 24-hour interval over a path between Deal, N. J., and New South-
gate, England, the radiated power being 1 kw. The curves bring out the advantages of
the higher frequencies by day and of the lower by night. A typical curve on an inter-
mediate frequency also is shown (10.55
me). Day-to-day variations are more
pronounced on such intermediate frequen-
cies than for either higher or lower fre-
quencies. On some days the intermediate
frequency transmission may resemble the
lower frequencies, on others the higher.
Variation with Distance. For a given
distance, the transmission conditions de-
pend on the geographical latitude of the
stations and to some extent on the geo-
magnetic latitudes, the difference in longi-
tude, the time of the day, the time of the
Mi
20
0
-20
-40
O OA
ghi_>j K<.Day--H }*- Night
i
j
i
27.51 Me
i
[/ ^
/ v
A
I -
/] r
\
I J
^
\
!
Y i
[
i
1
[
!/ ^^*>-^*"
\
21.42 Me
jr
>
|
/
\
=$.-40
5 20
§ °
i
/!
\
i
\
V J
l
\
\ J
1
1
1
I
i ^y<^- -i
16.27 Me
"V. J
l
/ j
\
2-40
0
55 20
1 '•
j
V!
x^
j /
,
^ >.
i
j
J
ii_
H>
.£-40
20
0
-20
-40
C
I j>
1
J
10.55 Me /
S\
y^*- /
V
v|— — ""--^t..
\ J
\ /
" \
1
1
\/
1
»
v
\
"J"-— ^
1
I
^
\
i
A
/ — ^^^~^^
\
/K
/
j
\! A
,/ i ^
6.755 Me
I
i \
r
\ L
\S.
i \ fe
1 !
« M 6"£ "£S>12 "S 18 E.S.T. 2^
II
year, and the time in the solar cycle. Fig-
ure 2 will serve as an approximate indica-
tion of the frequencies suitable for various
distances for day and for night. The
curves were based largely on data ob-
tained during the years 1926 to 1930, a
period which included a sunspot maxi- 5> 20
mum. In general, the frequency required
is higher the lower the latitude, the nearer
the time to noon at the midpoint of the
path, and the nearer to the secular sun-
spot maximum. In the winter the maxi-
mum usable (MUF) frequency for mid-
day is greater than in summer, but the
lowest usable high frequency (LUHF) is
lower. In a diurnal curve, the character-
istic day and night conditions are obtained
for a longer period the more uniform the
conditions along the path. Thus, a north-
south path has a more abrupt change from
day to night conditions than an east-west
path, and the transition condition is of
shorter duration. This transition period
is relatively difficult because no single fre-
quency can be best adapted to both the
day and night portions of the path. Hence, long east-west paths tend to be more difficult
than north-south paths. Usually, a day frequency gives a weaker field by day than a night
frequency does by night. The variation of best frequency with secular magnetic change
is exemplified by transatlantic paths such as that from New York to London. During
the sunspot maximum of 1930, the
best daytime frequency was about
18T000 kc, whereas, during the
minimum which followed, the best
was under 15,000 kc. (See later
discussion under "Maximum and
Minimum Usable High Frequen-
cies.*')
The Skip Effect. This effect is
in many ways analogous to the
phenomenon of total reflection in
optics. A light wave (Fig. 11)
Phenomenon of Total passing from one medium of dielec-
FIG. 10.
Diurnal Characteristics of High Frequencies
in Transatlantic Propagation
<tfw/""//'tfw/w>twy/^^
\< Skip Distance — *4
Transmitter '
FIG. 11. The Skip Distance as £
Reflection
trie constant n% into another of
smaller dielectric constant ni is
subject to reflection at all angles if the change in dielectric constant is abrupt, and to total re-
flection for angles of incidence greater than ^ = sin"1 ni/nz. In radio, the type of reflection
resembling total reflection is believed to be the more important, since the change in dielec-
tric constant is gradual. For large angles of incidence (incident ray approaching the hori-
10-42 TRANSMISSION CIRCUITS
zontal) the wave may be reflected to a great distance, but for angles less than the critical
angle ^ (closer approach to the vertical) the wave may pass through without substantial re-
flection. Although the radio problem is more complex than that of the optical illustration
owing to the gradualness of the change in refractive index brought about by the gradual
change in ionic density, in both cases the strong wave of total reflection is absent at the
smaller angles of incidence. Since the index, 712, of air at sea level is unity, waves incident at
the ionosphere at an angle less than sin"1 ni pass through. n\ is to be taken as the index of
the ionized region at the altitude of maximum ionic density (minimum refractive index),
and, since it is a function of frequency, time, and other factors, the skip distance is a func-
tion of the same factors. Figure 2 shows approximate values of skip distances, obtained
experimentally, for day and night conditions as a function of frequency. [Taylor and
Hulburt, Phys. Rev., Vol. 27, 189 (February 1926).!
Directions of Departure and Arrival. For a single wave component, this direction can
be expressed by two angles. One is that in the horizontal plane and can be given either
in terms of true north or as deviations from the great circle containing the transmitter.
The other is the angle in the vertical plane and is usually given as the angle between the
ray and the horizontal plane.
In the horizontal plane, the direction of arrival does not ordinarily deviate markedly
from the great circle, deviations greater than a few degrees being unusual.
In the vertical plane, the angle with the horizontal may be anywhere in the range from
0° to 90°, depending on conditions in the ionosphere, distance between stations, and fre-
quency. In general, as constructions such as that of Fig. 7 would indicate, the angle for
short paths is high. For long distances, the angles tend to be small. Thus, in transatlantic
communication, angles from 10° to 20° are common. Angles as low as 8° and as high as
38° have been measured. The average seems to be not far from 15°. On the other hand,
signals received near New York from Buenos Aires commonly arrive at vertical angles less
than 5°. In the case of the transatlantic paths, a great deal of attention has been given
to these questions by Friis, Feldman, and Sharpless, Proc. I.R.E., Vol. 22, No. 1, 47
(January 1934), and by Feldman, Proc. I.R.E., Vol. 27, No. 10, 635 (October 1939). They
found that the directions of individual wave components do not change rapidly or capri-
ciously; that the components which arrive at the higher angles arrive later than those at
the lower, qualitatively as might be expected from Fig. 7. In the vertical plane, angular
spreads between lowest and highest component have been found at times to be smaller
than 1° and at other times as large as 20°.
Polarization. In sky-wave transmission of high frequencies the composite polarization
of the received wave is on the average independent of that transmitted. The direction
of the electric field changes in a random manner with a rapidity which is connected with
that of fading.
Echoes of Long Delay. Among the more unusual echoes of long delay, two types
are of particular interest. Under certain conditions, "round-the-world echoes" can be
observed. These are waves having a delay of about 1/7 second, which travel all the way
along a path which probably is not very different from the great circle separating the day
and the night hemispheres. They are not usually observed but are prevalent at certain
times of the year for a given pair of stations.
A second type of echo exhibits delays as great as 30 seconds. This extraordinary retarda-
tion may be due to extremely low group velocities in the ionosphere or to waves which
travel long distances outside the ionosphere before they return. They are as rare as they
are mysterious.
Maximum and Minimum Usable High Frequencies. Several years ago the National
Bureau of Standards began a systematic study and publication of the month-to-month
variations in the ionosphere at Washington, D. C., with predictions of transmission con-
ditions to be expected. During the war this work was developed comprehensively. From
the point of view of operation, it is important to know for a given time and path the
maximum usable frequency (MUF) permitted by the skip phenomenon and the lowest
usaMe high frequency (LUHF) permitted by ionospheric absorption. Predictions on a
worldwide basis are available. (See publications of the Central Radio Propagation Lab-
oratory, National Bureau of Standards, Washington 25, D. C.)
23. OBSTACLES TO TRANSMISSION
ATMOSPHERIC INTERFERENCE. "Atmospherics" or "static" are electric waves
of natural origin which often mar radio reception or make it impossible. The sounds
prodiK^d vary from the crackling of extremely short impulses called "clicks," such as
may be produced by local lightning flashes, to the steady background roar called
OBSTACLES TO TRANSMISSION
10-43
* 'grinders." Hisslike atmospherics have also been observed. The principal characteris-
tics of atmospherics may be listed as follows:
1. They are more intense in summer than in winter, regardless of radio frequency. In
the northern hemisphere they reach their maximum in July or August. This leads to
more difficult transmission at that time.
2. They have a diurnal variation in intensity. For frequencies below about 10,000 kc
the night-time intensity is greater than the daytime. The difference is greatest at about
1000 kc in the vicinity of New York City, being perhaps 50 db, and is very small at 15 kc.
For the octave above 10,000 kc atmospherics are strongest in the daytime (see Fig. 12).
10,OUU
5000
2000
1000
~* ^
! Ill
J| |
1 1 ill
j
T • eu
'-
^
1 1 1
! 1
till!
T «
-*
>L /Variable
i
i 1 i I!
1-60 I
Intensity
t-»K> 01
3 01OO O
> ooo o
'X
"i'^FtJ
©Loca
I Thun
erse-F
1 ! f !!l j
derstorms
requency)
v
^•r^. fT3"
5" {Inv
T
-r40 *
t T-K
k , """-^
! i 1
xv
1
'^^.^
"-
©Average at Midnig
htJ §
s 10
° 5
5 2
« 0.5
« 0.2
01 0.1
0.05
0.02
0.01
N
! 1 1
^
b
? T-Q
i i
r20 c
•N t
II
'Sj
| i
j "-^
! i
\,®
Average
Midday
at
l^|l
i
H-4,
J2
f \
i h
\
_: o 1
. Based on *
Estimated
Note:
Only the slop
• cant. Us positi
. and B may cha
i i 1 I
rteasur.eme
s of curve
jn relative
nge consid
nt 'iL
!
t* — ^
h
,
/1
N
J
C is sigmfi-
to curves A
srably.
\
V
01
">.
/
\
20 oj
>~
_•"•*
^
\
...-40
0 kc 100 kc 1000 kc 10,000 kc 10O,OOO kc
Frequency
FIG. 12. Atmospheric Noise as a Function of Frequency in the Vicinity of New York City
The diurnal variation has a definite relation to the diurnal variation in the transmission
characteristics of the frequency used. [C. N. Anderson, Proc. I.R.E., Vol. 21, No. 10,
1462 (October 1933).]
3. The law of variation of amplitude of atmospherics with frequency cannot be simply
stated and is in fact not definitely known. Some evidence favors an inverse first, and some
an inverse second power. Figure 12 gives one estimate of the frequency distribution [H. K.
Potter, Proc. I.R.E., Vol. 20, No. 9, 1514 (September 1932)]. The figure is for reception
in the northeastern part of the United States; elsewhere the intensity and its distribution
with frequency would probably be somewhat different. By day the amplitude apparently
follows approximately the inverse square of the frequency up to 1000 kc. At higher fre-
quencies an increase having a maximum at about 15,000 kc sets in, but at this frequency
noise originating in the receiver is likely to be more important. The night curve seems to
follow the inverse first power up to about 10,000 kc. The advantage of low frequencies
due to better transmission is evidently reduced by the greater amount of atmospheric
disturbance encountered. Likewise, for the low frequencies, the advantage due to the
fact that the fields at night are stronger than day fields is similarly reduced by the fact
that atmospherics are then stronger.
4. Atmospherics are predominantly of tropical origin. Exceptions are those on inter-
mediate frequencies (500 to 3000 kc) during the day, and atmospherics on all ultra-
ionospheric waves. These are of comparatively local origin. On the low frequencies, less
atmospheric interference is found the farther the receiver is removed from the tropics.
For example, they are less in Maine than near New York. [Austin, Proc. I.R.E., June
1926, p. 373; Espenschied, Anderson and Bailey, Proc. I.R.E., Vol. 14, No. 1, 7 (February
1926).]
5. They are said to be stronger on land than over the ocean. [Austin, Proc. I.R.E,,
Vol. 14, No. 1, 133 (February 1926).]
6. Atmospherics arrive at a receiver from all directions, but usually certain general
directions predominate and over a small period of time the directivity may^be compara-
tively sharp. This is important in reception, since directional discrimination in the receiv-
ing antenna can be used to reduce the interference without reducing the desired signal; this
is not possible if the desired signal arrives from the same direction as the atmospherics.
When there is a variable null direction in the antenna polar diagram, the improvement ob-
tainable is very considerable unless the disturbances arrive through a wide range of angles.
[Espenschied, Anderson, and Bailey, Proc. I.R.E., Vol. 14, No. 1, 7 (February 1926).] ^
This directional characteristic is due to the existence of broad centers of origin which
seem to coincide with thunderstorm centers, most of which are over land. Among those of
greatest importance to reception in the United States are Ecuador, Brazil, and Central
Africa in the winter, and Mexico and Central America and the waters between there and
10-44 TRANSMISSION CIRCUITS
Florida, Florida, and New Mexico in the summer. The sources actually causing inter-
ference will depend on the distance range of the frequency used. Thus, frequencies of the
order of 1000 kc will have only local static by day, and ultra-ionospheric waves will never
be troubled by distant sources. At night, all services using the sky wave may be exposed
to distant sources. The very low frequencies are exposed to distant sources at all times.
(See papers by Dean and by Harper, Proc. I.R.E., July 1929, pp. 1185 and 1214.)
7. Atmospherics travel along the earth in the same manner as signals and are therefore
subject to the same laws of attenuation. Their diurnal variation is explained principally
by this fact.
8. Atmospherics apparently originate in discharges with sufficiently abrupt wave fronts
to shock-excite circuits tuned to any radio frequency lower than 150 me (or some higher
limit; see next paragraph). Components also fall in the audible range with frequencies
well below 1 kc. One class called "tweeks" has a limiting frequency between 1600 and
1700 cycles, suggesting multiple reflections of a pulse between the earth and a conducting
layer 90 km above it. [Appleton, Watson-Watt, and Herd, Proc. Roy. Soc., A, Vol. Ill,
165 (1926); Burton and Boardman, Proc. I.R.E., Vol. 21, No. 10, 1476 (October 1933) .j
9. At 150 me Schafer and Goodall ['Teak Field Strength of Atmospherics Due to Local
Thunderstorms at 150 Megacycles," Proc. I.R.E., Vol. 27, No. 3, 202-207 (March 1939)1
found (a) that the peak intensity of disturbances varies 20 db between different storms
at the same distance; (5) for nearby storms the inverse distance relation is a good approxi-
mation for the calculation of the variation of peak disturbance with distance; (c) the use
of high instead of low receiving antennas increases the signal-to-disturbance ratio almost
directly with height for storms within 10 miles; (d) the durations of some of the narrower
peaks in any particular lightning discharge are as short as a few microseconds or shorter;
(«) the maximum equivalent peak field for a storm 1 mile away was about 0.015 volt per
meter with a baad width of 1.5 megacycles. Although it is a common belief that atmos-
pherics do not exist at microwaves, actual measurements do not seem to have been reported.
10. Frequencies in the band near 20,000 kc exhibit distinctly an aural difference between
atmospherics from local and from distant sources. Atmospherics from local sources give
the * 'crash" type; those from distant sources ordinarily give a fairly steady weak back-
ground. The difference is not the result of any dissimilarity in mechanism but is due to
the skip effect which excludes disturbances from intermediate distances. The direction
of arrival of the steady background corresponds with that observed on long waves (SW
to SE near New York), and the disturbance is heard only when long-wave static is very
strong. As the frequency is increased into the ultra-ionospheric range, the steady back-
ground disappears, so to speak, in the distance, leaving only the crashes due to occasional
local storms. A weak hisslike disturbance apparently from a fixed direction in space and
from distances beyond the confines of our solar system has been observed on 20,000 kc. [K.
Jansky, Proc. I.R.E., Vol. 20, No. 12, 1920 (December 1932), and Vol. 21, No. 10, 1387
(October 1933).] Jansky pointed out that this noise arrived from the direction of the
galactic center (Sagittarius), and Reber [Asfrophysical Journal, Vol. 100, 279-287 (1944)],
at a considerably higher frequency which permitted high directivity, explored the region
of the Milky Way and found noise contours corresponding to it. Black-body radiation
from the sun has been studied by G. C. Southworth [J. Franklin Inst., Vol. 239, No. 4,
285 (April 1945)] at a wavelength of 3 cm; it may be looked upon as resistance noise, the
resistance being radiation resistance which has a high "temperature" when the antenna
points at the sun. An enormous increase in this noise has been reported to occur at times
of abnormal solar activity. [Pawsey, Payne-Scott, and McCready, Nature, Vol. 157, No.
39SO, 158 (Feb. 9, 1946), and Hey and Stratton, Nature, Vol. 157, No. 3976, 47 (Jan. 12,
1946).]
11. The noise level differs in different parts of the sunspot cycle. At high frequencies
there is a direct and at low an inverse relation to sunspot numbers.
12. Methods of combating atmospherics must be based on the use of some characteristic
in which the wave of the signal differs from that of the disturbance. The most important
of these are frequencyT direction, and amplitude. In the first, selective circuits are used
which suppress current of frequencies not present, or necessary, in the signal. Even with
absolutely ideal selective circuits, an irreducible minimum of energy will pass through them,
and this minimum increases linearly with the frequency range necessary for signaling.
(Carson, B.S.T.J., April 1925.) Directional discrimination has already been discussed in
paragraph 6 above. As regards amplitude, the most obvious procedure is to increase the
effective radiation toward the receiving terminal by increasing either the power capacity
of the transmitting set or the effectiveness of the transmitting antenna. Another is the
tise of tfee "compandor" in telephony, by which the low amplitudes are raised above their
masters! vakse wMle passing from the transmitter (through the part of the circuit exposed
to staospbeoGs) to the receiver, the normal values being usually restored subsequently.
OBSTACLES TO TRANSMISSION 10-45
An old method of discrimination against atmospherics of high amplitude uses opposed
detectors, equally sensitive at high amplitudes but sufficiently different at low amplitudes
so as not to cancel the signal. [Englund, Proc. I.R.E., Vol. 16, No. 1, 27 (January 1928).]
With amplitude modulation (in which intelligence is carried by variations of the ampli-
tude from its average value) improved signal-to-noise ratio can thus be obtained by limiting
the range of frequencies received and by increasing the amplitude variation at the trans-
mitter and simultaneously reducing the sensitivity of the receiver to changes in amplitude.
Analogously with frequency modulation (in which intelligence is carried by variations of
the frequency from its average value), the interfering effect of weak noises may be reduced
by limiting the range of amplitudes received, and by increasing the frequency variation
at the transmitter while simultaneously reducing the sensitivity of the receiver to change
of frequency.
Some forms, such as ignition noise, occur only in bursts which are very short compared
with the period of the signal being transmitted (e.g., in telephony, short compared with
the period of the highest audio frequency). It is advantageous in this instance even with
amplitude modulation to widen rather than narrow the frequency band of the receiver and
to use limiters; this widening, it is true, permits more noise power to pass into the final
detector, but it preserves the shortness of the impulse and permits the limiter to chop
off the peak, leaving a pulse no* greater than that of the signal and so short in duration as
not to be harmful.
FADING. In its most general sense "fading" means a reduction of the signal for any
cause, including, for example, the slow decrease in long-wave signal strength called the
"sunset minimum^" which may last an hour or so. Cornmonly the term refers to the more
rapid variations encountered with medium and short waves. Probably the most im-
portant cause of fading is the interference of wave components f oHowing different paths in
space, combined with variations of phase of one or more components with time. The
existence of the different components can be due to multiple reflections or to double refrac-
tion due to the earth's magnetic field, and perhaps other causes. The changing with time
of the relative phases can be due to change in the ionic density along the path or to changes
in the magnetic field. Pulse experiments, which are able to resolve a complex signal into
many components, show that, with the best resolution possible, the components themselves
fade. Fading is therefore a very complex phenomenon.
An important example of fading occurs just outside the service area of a high-power
broadcasting station. With increasing distance the sky wave finally becomes appreciable
compared with the rapidly attenuating ground wave. Atmospheric vagaries make the-
relative phase of the components vary at random, causing the signal level to fluctuate-
It may be further complicated by the reception of more than one sky-wave component*
(See article 24.)
Rapidity of fading of ionospheric waves increases, in general, with frequency. Below
100 kc the phenomenon is scarcely noticed; such changes as do occur commonly require
an hour or so. At 1000 kc the period is of the order of 1 minute, and the amplitude range
extreme. At 10,000 kc the fading rate is 1 every few seconds. Fading due to interference
between two or more components should show this characteristic, for a fade would then
occur onee for every change of 1 wavelength in the path difference. This relation, of course,
can be only qualitative, since long waves and short waves usually travel over very different
paths, are frequently not used at the same time of day, and do not employ the same number
of paths.
A distorted frequency characteristic is one of the results of transmission over two or more
interfering paths. Thus, if the times required for the waves to travel over the two paths
differ by r, and if the radio frequency is slowly varied, consecutive maxima and ininima
will be found, the frequencies of the maxima differing from one another by integral multi-
ples of 1/r. If r = 0.0005 second, a typical value, the maxima will be separated by mul-
tiples of 2000 cycles per second, and even the a-f characteristic may be seriously affected.
There will now be fading provided that a change occurs in the medium. Being a function
of radio frequency, such fading is called "selective." If T were made very small, the fre-
quencies of the maxima would differ so much that within the srrm-H band occupied by a
telephone channel the response would be independent of frequency. This would be non-
selective, or "general/* fading. The selectiveness of fading is thus associated with the
time difference over the two paths, whereas the rate of fading is related to the rate of
change with time of path difference measured in wavelengths. It is common to have more
than two components in a received wave. In some cases the wave is extremely complex.
[Potter, Proc. I.R.E., Vol. 18, No. 4, 581 (April 1930).]
As shown by Bown, Martin, and Potter [Proc. I.R^B.r Vol. 14, No. 1, 57 (February
1926)}r this mechanism can produce serious distortion in a speech channel if the instantane-
ous frequency of the transmitter varies during the audio cycle.
10-46
TRANSMISSION CIRCUITS
The change in field strength with frequency at a single receiving location has its counter-
part in a change with location for a constant frequency. The different paths differ not
only in length but also hi direction. Most important perhaps is the direction in the
vertical plane, as shown in Fig. 7, but the directions in the horizontal plane are also sig-
nificant. It is these directional differences which cause the difference in signal levels at
nearby points, for the two waves give rise to a set of interference fringes. Fading does not
therefore occur simultaneously at nearby points, and it is found in the high-frequency
range that points separated by 10 wavelengths usually fade in an unrelated manner,
whereas in some cases the separation need be no greater than 2 or 3 wavelengths. Advan-
tage of these facts is taken in "diversity systems" of reception, which employ receivers
operating on the same frequency from separate receiving antennas at different locations
or different polarizations, or on different frequencies from the same antenna. [Beverage
and Peterson, p. 531, and Peterson, Beverage, and Moore, Proc. I.R.E., Vol. 19, No. 4,
562 (April 1931).}
The effect of fading is to degrade the performance of a circuit used in communication.
This can be due merely to reduction of field during the fades, which leads to an inadequate
ratio of the signal strength to the noise. It can be the result of the distorted a-f character-
istic which was mentioned above; to the production of distortion products, as for example
when the carrier in a double sideband system fades out, leaving the two sidebands to beat
with each other; to the existence of fading so rapid that it cannot be compensated by such
devices as the automatic volume control, and to other complications. Probably the most
usual example of circuit impairment occurs when fading and noise contribute simultane-
ously. All such effects are the more serious the higher the standard set for the circuit.
SOLAR DISTURBANCES. Radio transmission is one of the terrestrial phenomena
which may be correlated with solar activity; another is the variations which occur hi the
earth's magnetic field, extreme
fluctuations having been given the
name "magnetic storms." Except
for daylight transmission with low
frequencies (e.g., 60 kc) the effect
of unusual solar activity is an ad-
verse one. By day, low frequencies
are then somewhat aided, but at
night their fields are considerably
reduced. The most marked effect,
however, is produced on the high
frequencies; in fact, very severe
storms may completely eliminate
their usefulness over some paths.
These effects are illustrated in Fig.
13, which shows daytime field
strength on two transatlantic chan-
nels, one (full line) on 18,000 kc
and the other (heavy dashes) on 60
kc, together with the horizontal
component of the earth's magnetic
field (light dashes). [Anderson,
Proc. I.R.E., Vol. 17, No. 9, 1528
Strengths In db
- i i + i
no 01 O 01 o
j
<T» 0^ O» Oi vl v| u
O> ^1 00 ID O M 00
O O O O O O -J
H Component of r>
Earth's Magnetic Field
i
•••s^^
X
>
'— -<
>x
\
/f
£/-
' 'N
' —
r>
v
/
\
/
\
^
/
,
^'
•*"""
T3 la
E -20
-25
~3Q
l\
/I
^^*
/
/
r*- "
\
/
/
\
(/
54321012345678
Days Before Storm Days After
^ oTraasraissloo on 18,34 MC (IB Meters) Deal. HJ. to Hew Southgate, England.
<*— -sTransroission on 60 Kc.(5000 Meters) Rocky Point, LI. to Cupar, Scotland.
»- -- -tfodrontil Component of Earth's Magnetic Field.
FIG. 13. Typical Effects Accompanying Magnetic Storms
(September 1929).] A striking demonstration that rapidly moving ionic clouds are hurled
into the ionosphere during magnetic storms has been given by Wells, Watts, and George
of the Carnegie Institution of Washington by a technique of rapidly recording the reflec-
tions received over an extended frequency range.
^The solar phenomena include sunspots, prominences, and flocculi which may be observed
with a telescope or spectrohelioscope. The disturbing areas rotate with the sun once in
every 27 days, this being the reason for the ill-defined "period" of 27 days in the terrestrial
effects. In order to have a terrestrial effect it seems to be necessary that the disturbed
solar area have a certain orientation with respect to the earth. The 27-day period in
magnetic and radio effects forms the basis for a method of predicting future disturbances;
these predictions, though not entirely reliable, are useful. Another periodicity in solar
activity is the secular one, having a cycle of about 11 years. Since the last minimum and
maximum occurred respectively in 1944 and 1947, it appears that the next will take place
about 1954 and 1958.
Depending on the severity of the "storm," the effect may last one or several days, during
which communication on short waves is erratic and difl&cult and sometimes impossible.
At the same time, the aurora may be visible, earth potentials usually rise to relatively
RANGE OF RADIO STATIONS, BROADCAST COVERAGE 10-47
80
545
"
|4Q
\
Magi
(Horiz
\
\
\
90
80
270
feo
!«°
§30
<°20
10
0
\
\
\
stic Actlvi
ntal Ran
Sig
/\
high values, and the earth's magnetic field may be seriously disturbed. Short-wave
transmission along paths through equatorial regions are scarcely affected, however; it is
in the auroral zone that the effects are produced, and, apparently, high-frequency trans-
mission over any path, long or short, which requires reflection from the ionosphere in this
zone, is adversely affected. At such times, experiments to determine virtual heights in
these zones are impossible owing to the total absence of reflections. [Appleton, Naismith,
and Builder, Nature, Vol. 132, No. 3331, 340 (Sept. 2, 1933).] The secular period in this
effect has already been mentioned. Figure 14 illustrates this variation, which follows
the 11-year sunspot cycle.
[Austin, Proc. I.R.E., Vol. 90
20, No. 2, 280 (February
1932).]
Another phenomenon as-
sociated with the sun is the
radio fade-out, during which
all sky waves except those
of low frequency are sud-
denly weakened or obliter-
ated over the earth's sun-lit
hemisphere. It has been
established that the fade-
out is coincident with a
bright solar chromospheric
eruption, and the absence of
the effect at night and its
great intensity at the equa-
tor indicate ultraviolet light
rather than particles as the
means by which it is pro-
duced. A fade-out may last
from a few minutes to a few
hours. It is evidently
caused by an unusually high
electronic density produced
below the .S-region which
operates by absorption due
to the high collision fre-
quency with neutral mole-
cules at that level. [J. H.
Bellinger, Science, Vol. 82,
No. 2128, 351 (Oct. 11,
1935) ; L. V. Berkner, Phys.
Rev., Vol. 55, No. 6, 536
(March 15T 1939).]
An abnormality known as sporadic E layer reflections is of some importance as the cause
of occasional long-distance transmission at frequencies above the usual ionospheric limit,
sometimes as high as 60 me. It occurs in patches rather than uniformly over the E layer
and is not well understood. [L. V. Berkner and H. W. Wells, "Abnormal lonization of the
^-Region," Ter. Mag. and Atmos. Elec., Vol. 42, No. 1, 73 (March 1937).]
inspot N
\
Years
FIG. 14. The "1 1-year" Period in Sunspot Activity and ItsjCorre-
lation with Magnetic Activity _ and Low-frequency Radio Trans-
mission
24. RANGE OF RADIO STATIONS AND BROADCAST COVERAGE
The distance over which communication can be carried on, or the "range" of a radio
transmitting station, depends on so many changeable phenomena and special details that
the term is usually significant only as an order of magnitude or as a statistical mean. The
range depends on transmission efficiency and noise (e.g., atmospherics), on the types of
apparatus used at the receiving station, and on the standards of performance. More
meaning attaches to the range of a ground wave, however, because of its steadiness relative
to the ionospheric wave. The service range of a broadcast station may be set by noise
due to atmospherics, to industrial or domestic electrical equipment, or to unavoidable
random noise arising in the receiver itself. But even when noise is negligible it may be
limited by fading due to the sky wave's being appreciable compared with the ground wave.
Considering noise as the limiting factor, we may start with representative noise data
such as those given in Fig. 15. This figure gives approximate noise values (atmospherics,
10-48
TRANSMISSION CIRCUITS
set noise, etc.) which we assume as typical for medium-frequency broadcast reception in
northeastern United States in the summer. For reception the signal field must be greater
than the noise by certain values which depend on the grade of service desired. This leads
to a required signal field, and the distance at which it is obtained under certain conditions
can be obtained by reference to Fig. 3. For example, to find the summer night range of
the ground wave of a 100-kw transmitter operating on 1500 kc, we have:
Summer midnight noise on 1500 kc, Fig, 15 0.035 mv/meter
Signal-to-noise ratio assumed ' 100
Field required with 100 kw radiated^ 3.5 mv/meter
Field with 1 kw radiated (3.5A/100) • 0.35 mv/meter
Distance giving 0.35 mv/meter (51 db above 1 mv/meter) with 1 kw,
<r = 2 X 10~13, Fig. 3 53 miles
Figures such as these, which are based on transmission data applying in the ease of level
terrain, cannot in general apply if there are large obstacles or other irregularities in the
path. A striking example of
1,0 c — —
0.1
I
0.01
: Noise Level vs Frequency .;
' ftjninj
this was described by Bown
and Gillette, who found
that sections of New York
City in which there are large
numbers of unusually tall
buildings cast "shadows"
for several miles [Proc.
I.R.E., Vol. 12, No. 4, 395
(August 1924)]. Dense
areas of small buildings also
reduce the range. There
are other factors than noise,
such as fading and interfer-
ence from other stations,
that complicate this prob-
lem and require consider-
able experience to assess.
Field strength surveys of
the actual territory to be
covered are frequently re-
quired. [Standards of Good
Engineering Practice,
F.C.C., loc. cit.;R. F.Guy,
loc. cit.; "An Analysis of
Continuous Records of Field
Intensity at Broadcast Fre-
quencies," Norton, Kirby,
and Lester, Proc. I.R.E.,
Vol. 23, No. 10, 1183 (Octo-
ber 1935); "On the Use of
Field Intensity Measure-
ments for the Determina-
tion of Broadcast Station
Coverage," Jansky and
Bailey, Proc. I.R.E., Vol.
20, No. 1, 62 (January
1932).]
Another limitation in the
service area of a broadcast
station in the evening is the existence of fading beyond a certain distance. This limiting
distance depends on frequency and earth conductivity, and in general it is greater the
lower the frequency and the higher the conductivity. Fading first becomes serious when
the sky wave becomes appreciable compared with the ground wave. Figure 16 illustrates
as a function of frequency, how the distance range of broadcast stations depends on
electrical noise and fading, an earth conductivity of 10~13 being assumed. [Report of Com-
mittee on Radio Propagation Data, Proc. /.£.#., Vol. 21, No. 10, 1430 (October 1933) ]
i o.ooi
I
0.0001
0.00001
8 S
800000000
oooooooo
o O 1-1 CM to ^rtnto pv
Frequency - Kilocycles
FIG. 15. Typical Noise Data, Broadcast Reception
TRANSMISSION-LINE CONSTRUCTION
10-49
Midnight
1000,
Mtfday*
Ground Wave Transmission Only
Kilocycles
8 8
CNJ «*
Variations with Changes in Power
800
600
400
52200
<o
lioo
o 80
5 60
40
20
10
<
_i
b
^N
•^,
ai
N<
ie-
w
Su
Yo
lo
mr
rk-
id,
•>-.
ne
Su
i-S
r, -
mn
ur
F
ner
•im
or
da
-W
nt
er
s.
— —
i*!
•••.
••^
—
==
Power 1 Kw
% Ratio^i
Minimum Noise .01MVw
= 888888888
Kilocycle
Variations with Changes in Noise Level Kilocycles
auu
600
400
2200
£100
-*.
•«v
^:
•**»
-».
s,
x
v
^
--.
•-v
••».
••»,
-^.
-«.
iti
> 1
k
^ 60
40
20
zr4'
YI
Min
Power 1 Kw
mum Noise .01M>w
1
8888888
-- CO O CM ^ u> w
Kilocycles Kilocycles
Variations with Changes in Signal-to-Noise Ratio
*Assuming most favorable daytime conditions and
limiting background noise of .01, in^millivolts per
meter throughout the frequency ranga.
FIG. 16. Useful Hange of Broadcast Stations under Different Conditions of Power, Noise Level,
and Permissible Signal-to-noise Ratio. Central United States and Europe.
MECHANICAL FEATURES OF TRANSMISSION LINES
By John D. Taylor
25. TRANSMISSION-LINE CONSTRUCTION
POLE LINES are employed in aerial communication construction to support open
wires and cables used in toll and exchange plant. The supporting structures are generally
of wood but, for special requirements or where pole timber is not obtainable, may be of
steel or 'other materials.
The use of wood poles generally throughout the United States and other countries is
due principally to (1) availability, (2) economical type of construction, (3) ease of handling
and maintaining, and (4) relatively long life.
The design of wood-pole lines is based primarily on (1) type of communication plant
(toll or exchange) to be supported, (2) load to be carried, and (3) location and exposure to
weather. The poles must be of sufficient strength (allowing for ground decay and econom-
10-50
TRANSMISSION CIRCUITS
ical life) and height (allowing for ultimate loads and required clearances) to meet the
requirements for this type of construction in the most economical manner.
In exchange plant, initial pole-line routes largely determine the routes of distribution
for succeeding types of construction, while for toll plant the large initial costs involved in
building a toll pole line usually require its maintenance on the selected route, at least for
its economical life or until other considerations such as right-of-way, growth, new develop-
ments or deterioration necessitate its removal or replacement. In planning new pole lines
or rearrangements, it is important to so advise other pole-using companies in the area
involved, in order that the plans of all the companies may be in coordination at all times.
The selection of the pole route usually entails advance surveys, acquiring the necessary
right-of-way, and other considerations, which will provide the required pole line econom-
ically. Due regard must be given to the future adaptability and relation of the pole line
with respect to the telephone system, serving the area, as a whole. Toll pole lines usually
take the most direct, practicable route between terminating points, avoiding small towns,
trees, and hazardous conditions as far as possible. Toll points, off the main toll route, are
reached by branch (spur) lines. Along highways, one side should be occupied throughout,
as consistently as conditions permit, avoiding unnecessary road crossings and leaving the
other side of the highway for other wire-using companies.
Public right-of-way is less expensive initially, but private right-of-way for a particular
section of pole line may result in lower annual charges and ultimate costs and most cer-
tainly will add to the permanence and safety of the line.
Joint use is generally desirable and economical in urban areas, rather than using
separate pole lines for power and telephone facility distribution. The power circuit
vohages in cities are usually low (not over 5000 volts), and the telephone equipment and
subscribers axe adequately protected in case of contact between the power and telephone
circuits.
Joint use with rural or toll open-wire circuits is not, as a rule, desirable, because of the
generally higher-power circuit voltages and of possible hazards to life and property from
contacts. Consideration may be given, however, to such joint use in any particular case,
and future developments may indicate its desirability for rural construction.
The selection of poles required for any particular pole line is based mainly on (1) the
number of telephone or other aerial wires and cables to provide facilities over the expected
service life of the poles, (2) the importance of these facilities, (3) the pole strength required
to carry the initial and ultimate wire and cable loads under the weather conditions ex-
pected in the locality involved, and (4) governmental regulations.
Some companies have established classifications for open-wire and cable pole lines, in
accordance with the service value of the line (relative importance and number of messages
carried by the circuits on the line). Figure 1 shows the classifications used by the Bell
System and the relative strengths assigned based on the System's experience. Lower
percentages of ultimate stress are required for railroad, power, or similar crossings.
Classification
of Line
Type of Service
Message-
miles
per day
Relative
Strength
Levels
Maximum Percentage of
Ultimate Fiber Stress
under Transverse Loading
For New
Poles
At Replace-
ment
A
Toll open-vrire and cable of
high service value
Over 30,000
100
45
67
B
Toll open-wire (average serv-
ice value) and toll cable
(not class A)
5,000 to
30,000
67
67
100
C
Exchange open- wire (over 10
"wires), all exchange cable. . .
50
89
133
Toll open-wire of low service
value
Less than
5,000
50
89
133
R
Exchange open-wire (not over
1 0 wires)
33
133
200
J
Joint power and telephone
lines
88
50
75
FIG. 1. Classification and Strength Requirements of Pole Lines, Bell System Practices
TRANSMISSION-LINE CONSTRUCTION
10-51
In connection with the preparation of the National Electrical Safety Code (N.E.S. Code) ,
National Bureau of Standards Handbook H32, studies were made to determine the fre-
quency, severity, and effects of ice and wind storms throughout the country. On the
basis of these studies, three general loading areas, heavy, medium, and light, were estab-
lished for the United States, as shown in Fig. 2. For the same classification of line and
other structural condi-
tions, a heavier class of
pole is required (particu-
larly for average or greater
loads) in the heavy than in
the medium or light load-
ing areas, and likewise in
the medium as compared
to the light loading area.
Basic conductor load-
ings have been assigned
for the three loading areas,
in order to derive pole
loadings, considered ap-
propriate for these areas,
and with the various pole-
line classifications and
other data, to arrive at the
class of pole required for
any given line. Figure 3
shows these assumed load-
ings and associated constants, which latter, when added to the resultant of the vertical
and horizontal loads, will result in effective conductor loadings, substantially the same
for the Fifth Edition as for the Fourth Edition of the N.E.S. Code. Thus, it has been
possible to avoid lowering past overall effective standards for pole-line strength require-
ments, and at the same time to reduce, in the Fifth Edition, the transverse loadings on the
pole line to permit the use of allowable stress values more nearly representative of general
engineering practices.
Assumed Vertical and Transverse Loadings
G. 2. Storm Loading Map of the United States (from N.E.S. Code,
Fifth Edition, Natl. Bu. Stds. Handbook H8£)
Radial Thick-
Horizontal Wind
Storm
ness * of Ice
Pressure at Right
Loading
Symbol
Coating on
Angles to the Line,
Area
Conductors and
lb/sq ft of
Messengers, in.
projected area
Heavy
H
0.50
4
Medium. ......
M
0.25
4
Light
L
None
9
* Note: In computing transverse loading on poles and towers, ice coating on these structures is
ignored.
Constants for Various Types of Conductors to Be Added to the Resultants of the Loadings
Shown in above Table, pounds per foot
Storm
Loading Area
Sym-
bol
Tem-
pera-
ture,
degF
Bare Copper, Steel,
Copper Alloy,
Copper-covered
Steel, and Combi-
nations Thereof
Bare Aluminum
with or without
Steel
Reinforcement
Weather Proof
and Similar
Covered
Conductors
(AH Materials)
Cable
with
Messenger
H
0
0.29
0.31
0.31
0.6
M
+ 15
.19
.22
.22
.4
Light
L
+ 30
.05
.05
.05
.2
Note: For telephone wires it is usually assumed that
P = 0.003 V2
where P — horizontal wind pressure in pounds per square foot of projected area.
V — actual wind velocity in miles per hour.
FIG. 3. Assumed Vertical and Transverse Loadings and Associated Constants (from N.E.S. Code,
Fifth Edition, National Bureau of Standards Handbook HSS)
10-52
TRANSMISSION CIRCUITS
Since pole lines carry various types of communication facilities and frequently (on joint
lines) power conductors and equipment as well, it is necessary, in determining pole-line
loads, to equate the various attachments to a common basis. Figure 4 gives wire equiva-
lent data for the three loading areas in terms of effective 104 (mil diameter) telephone wires
and of effective No. 4 covered power wires. In heavy and medium loading areas only,
Attachment
Telephone Wire Base
(Effective
104 Tel. Wires)
Power Wire Base
(Effective No. 4
Covered Power Wires)
Storm Loading Area
Storm Loading Area
Heavy
Medium
Light
Heavy
Medium
Light
Communication plant
Bare open wire, 109, 104, or smaller, per wire
Bare open wire, 128, 134, or larger, per wire.
Covered paired wire, per pair, or covered
1
1
1
2
4
5
6
7
1
1
1
1
8
4
1
1
1
2
5
6
7
8
1
1
1
14
7
I
1.3
2.5
5
15
22
30
35
4
6
4
2
50
25
0.8
0.8
0.8
2
3
4
5
6
1
1
1
3
0.7
0.7
0.7
2
3
4
5
6
1
1
1
0.5
5
0.3
0.4
0.7
2
4
6
8
10
1
2
1
0.5
8
Cable and 1 0 000 Ib (3/8 i11-) strand
Cable and 1 6,000 Ib (7/16 in ) strand . ...
Cable and 25 000 Ib (1/2 ^ ) strand
Cable terminal, "B" or "BB" type, 202 pair
and less or "BD" type, all sizes
Cable terminal, "B" or "BB" type, more than
202 pair
Cable loading pot - - - - - •
Service drops 'per unbalanced drop
Clothes-lines on Class C line poles, per unbal-
GLolhee-lines on Class J line poles, per unbal-
Power plant
Covered wire, No. 8 AWG (approx. 0.26 La.
o d ) or smaller per wire
1.1
1.2
1.3
1.5
2
3
3
6
6
12
18
2
3
5
1
1
1
I
I
1.3
1.4
1.5
1.9
3
4
5
7
10
20
30
2
3
6
1
2
2
1
1
2.5
3.1
3.7
6.3
11
15
20
30
25
50
75
8
9
19
6
9
4
3
3
0.9
1.0
1
1.2
2
3
3
5
5
10
15
2
3
4
1
1
1
1
1
0.9
1.0
1
1.3
2
3
4
5
7
14
21
2
2
4
2
2
1
0.7
0.9
1
1.7
3
4
6
8
7
14
21
2
3
5
2
3
1
1
1
Covered wire, No. 6 AWG (appro*. 0.32 in.
o d.) per wire
Covered wire, No. 4 AWG (approx. 0.38 in.
o d ) per wire ...
Covered wire, No. 0000, AWG (approx. 0.65
in. o d.) per wire
Covered wire, 500,000 circ mils (approx. 1.11
Covered wire, 1,000,000 circ mils (approx.
1 53 in o d.) per wire . .
Covered wire, 2,000,000 circ mils (approx.
215 in. o.d.) or larger, per wire
Power cable on strand (approx. diam. of
cable 2 56 in or less) . . .
Suspension wire extend-
ing transversely be- One contact wire
tween two pole lines Two contact wires
and supporting trolley Four contact wires
contact wires, per line
Bracket and one trolley contact wire on one
side of pole line
Brackets and two trolley contact wires, one
on each side of pole line ... - . . ...
Bracket and two trolley contact wires, over
tracks on same side of pole line
Tr&Tvgforrnpns 37 l/o fc-u-a or less
Transformers, over 37 !/•> kva
Transverse clearance attachment for service
drop above telephone attachments, per wire
Service drops, per unbalanced drop wire
Street lamp supported by mast-arm (not
bracket) ,
Table of Wire Equivalents for Pole-line Loading Calculations (from NJS.S. Code, Fifth Edition,
Notional Bureau of Standards Handbook HS%}
TRANSMISSION-LINE CONSTRUCTION 10-53
when the actual number of wires on crossarms is more than 10, shielding reduces the effec-
tive number of wires to 67 per cent of the actual number. In light loading areas, loading
is assumed on actual wires.
The selection of new poles for a given pole line requires that the following factors be
known or assumed:
(a) Classification of pole line (determines the relative importance of the line),
(6) Loading area (determines the basic loadings).
(c) Fiber strength of timber to Table 1
be used (see Table 1).
Type of Timber
Fiber Strength,
Ib/sq in.
Northern white cedar
"Western red cedar
Creosoted southern pine and Douglas fir. .
Chestnut.
(d) Equivalent (effective) tele-
phone wire or power wire load
(see Fig. 4).
(e) Average pole spacing (de-
pends on type and size of wire,
usage, loading area, and class of
line for open wire) .
(/) Length of poles (deter-
mined by load and clearance re-
quirements).
If tables are not available for determinrng directly the class of poles required under the
above known or assumed conditions, the following formulas may be used for the purpose.
For transverse loading (pole acting as a cantilever beam)
Lodge pole pine .
Juniper
Cypress
3600
5600
7400
6000
6600
4600
5000
c =
0.0002&4/£/
where C — minimum required ground line circumference of new pole in inches.
Mw — resistant moment on pole at ground line, due to wind pressure on wires, in
ft-lb.
- PDLNS.
P SB wind pressure, in Ib/sq ft.
D = diameter of each wire, in ft, including ice coating, if any.
L » distance, in ft, between center of the load and the ground line section.
N = effective number of wires on the pole.
S = 1/2 sum of the two adjacent spans, in ft.
Mp — resistant moment on pole at ground line, due to wind pressure on pole, in ft-lb.
where h = height of pole above ground, in ft.
Ct — circumference of pole at top, in in.
Cg = circumference of pole at ground line, in in.
U = maximum percentage of ultimate fiber stress expressed as a decimal (determined
from the line classification, Fig. 1, or as required) .
/ == maximum allowable fiber stress of the pole timber, in Ib/sq in.
For vertical loading (usually considered only for anchor guyed poles or stubs, where the
vertical component of the stress in the guy may be large), the pole is considered to be a
long column, and by Euler's formula for such a column
P.-MBg
where Pv — vertical load on the pole, in Ib.
JLI = x2 for average conditions of a guyed pole or stub.
E — modulus of elasticity of the pole timber.
/ = moment of inertia of the critical section (see note) .
I — length of the column, in in., from the point of anchor guy attachment to the
butt of the pole (for poles set in solid bases, such as rock or concrete, the
length is taken from the point of anchor guy attachment to the ground
line and & = 27T2).
Note: The critical section in flexure for the average pole (of conical shape) is assumed
to be at a distance of Vs I below the point of anchor guy attachment. The circumference
of this section should be computed from (1) its distance above a point, which is 6 ft from
the butt of the pole, (2) the specification circumference 6 ft from the butt, and (3) the
average circumferential taper for the timber under consideration.
In general, the size of line pole, selected for the ultimate load, is determined by the
transverse stress, to which the pole may be subjected. There may be cases, however,
10-54 TRANSMISSION CIRCUITS
where the vertical load, particularly where large transformers are mounted near the top
of the pole, becomes a substantial factor in determining the pole strength required.
In such cases, both transverse and vertical stresses and their resultant stress may need
to be determined, although the vertical and combined stresses can only be calculated
approximately.
A wood pole is considered as a long tapering column, which, under a critical concentric
vertical load, fails by buckling. The maximum load that the pole can safely carry de-
pends on the degree of freedom of the pole ends, the distribution and arrangement of the
vertical loading on the pole, the support given the pole by any wire or cable attachments,
and other variable factors.
For wood, the maximum compressive strength is considerably less than the modulus of
rupture and the maximum allowable stress for the combined compression and bending
stress is intermediate between these two values.
Methods have been developed for determining approximately the combined stress on
a pole at the ground line, due to vertical (axial) and transverse loads, under certain as-
sumptions, but, because of their complexity, these methods are not discussed in this
handbook.
Where it is desired to employ such methods, reference may be made to Provisional
Report Xo. 24 (Technical Report 2G-2), A Study of Pole Strength in Jointly Used Poles,
of the Joint Subcommittee on Development and Research of the E.E.I, and B.T.S. of
August 22, 1938.
The minimum required ground-line circumference of the pole C having been determined,
the class of pole actually selected from the ASA Specification Tables should have a ground-
line circumference at least equal to the minimum required ground-line circumference C
plus an amount of wood which, based on average decay rates for the timber and location
involved, will provide the desired service life in accordance with the formula
C, - C + y(L - T)
where Cg = minimuni ground-line circumference of the new pole, in in., to provide desired
service life.
C — minimum required ground-line circumference of new pole, determined as
above.
y — average rate of decay of untreated timber in equivalent inches of circumference
per year. (For the cedars and chestnut, this decay is about 0.45 in. for
sap wood and 0.3 in. for heartwood per year. For southern pine the physical
life is about equal to the effective period of treatment.)
L — desired physical life in years.
T = expected life of preservative treatment in years (probably roughly 20 years
for initial treatment of butt-treated poles).
The ASA (American Standards Association) Specification Tables of Pole Dimensions,
referred to above, are readily available and are based primarily on:
1. Fiber strengths of various timbers used.
2. Ten classes of poles (1 to 10) with Tm'mrrmm circumferences for 6 ft from the butt
specified for classes 1 to 7, and minimum circumferences at the top of the pole specified
for all classes.
3. Breaking loads 2 ft from the top for the first seven classes in approximate geometric
progression as follows:
Class Breaking Load, in Ib
1 4500
2 3700
3 3000
4 2400
5 1900
6 1500
7 1200
4. All new poles of the same class and length (classes 1 to 7 only) to have about equal
resistant moments at the ground line.
5. All new poles of the same class (classes 1 to 7 only) to be of such size as to have about
the same breaking load, with the load applied 2 ft from the pole top and assuming that
the break would occur at the ground line.
Treatment of poles to prolong their physical life is standard practice. The preservatives
used may be creosote, greensalt, or other chemicals toxic to wood-destroying fungi and
wood-boring insects. The creosote treatment may be applied the full length of the pole,
as in southern pine, under a pressure and vacuum with a net retention normally of 6 to 8
Ib of creosote per cubic foot of wood, and a penetration of not less than 2 1/2 in. or 85 per
cent of the sapwood. Greensalt is also applied to poles by the pressure method, and it
has some advantages over the creosote treatment. Butt-treated poles, such as the cedars,
TRANSMISSION-LINE CONSTRUCTION
10-55
are usually processed in open tanks of hot and then cold creosote, the ground-line section
being incised to assist penetration, which averages about 0.4 in. or more.
The spacing of poles depends largely upon the type of the wire or cable load, location,
transposition scheme, and exposure to storms. For important backbone toll routes the
spacing is generally about 130 ft for open wire and from 150 to 300 ft for toll cable.
The guying of pole lines is necessary at points of above average stress, such as at corners
having substantial pulls, dead-end poles, and poles carrying unusual loads. Guying is
also applied on toll lines at periodic intervals along the line to assist the pole-line structure
in withstanding storms. The ratio of lead to height of guys should be about 1.0 to 1.25,
the guy stress then being about 1.4 to 1.28 times the horizontal stress.
Cross-arms are designed to carry from 2 to 10 or 12 wires, as may be required for any
particular case, and may be fitted with locust or steel pins, usually spaced from 6 to 12
in. for telephone and 10 and 11 1/4 in. for telegraph wires (16 to 30 in. for pole pairs). The
cross-arms are usually spaced 24 in. apart vertically on the pole and vary in number per
pole from 1 to 6 or more.
OPEN WIRE, supported on insulator-equipped cross-arms or brackets, which are in
turn mounted on poles or fixtures, has been employed since the invention of the telegraph
and telephone to connect individual instruments to wire centers or offices, and one office
to another. However, wire conductors enclosed in lead sheaths (cables) have practically
superseded open wire in built-up communities and cities and in large measure, for tele-
phone communication, have replaced or supplemented open-wire lines between the prin-
cipal cities.
The types of open wire employed for telephone communication circuits, as discussed in
Section 17, consist principally of 104, 128, and 165 hard-drawn copper and some 104 and
128 copper steel (40 per cent cond.) for toll circuits, 080 copper steel (40 per cent cond.),
and 080 and 109 high-tensile steel for exchange circuits in outlying areas (all given in mil
diameter). High-tensile steel wire, because of the pole economies realized, its greater
strength, and its equally good service performance, is being employed for new construction
generally in place of the various grades of mild steel and iron wire.
The types of open wire employed for telegraph communication circuits consist mainly
of 114 hard-drawn copper, 162 copper steel (40 per cent cond.), and some 165 iron for
important facilities.
Drop wires of various types are used for both services.
Table 2 shows some of the important physical properties and the electrical resistance
of wire, classed as open wire, for both telephone and telegraph circuits. Other electrical
characteristics of various types of wire are discussed in Section 17.
Table 2
Type of Wire
Wire
Number
and
Gage
Nominal
Wire
Diameter,
in mils
Average
Weight
per Wire,
in Ib/mi
Minimum
Breaking
Strength
per Wire,
inlb
Average
Resistance per
Loop Mile,
in ohms
at 68° F
Telephone
Hard-drawn copper
14-NBS
80
102
330
17 50
Hard-drawn copper
12-NBS
104
173
550
10. 15
Hard-drawn copper . .
10-NBS
128
262
819
6 74
Hard-drawn copper
8-BWG
165
435
1325
4.11
Copper steel (40%)
14-NBS
80
96
770
42 8
Copper steel (40%)
1 2-NBS
104
159
1177
25.0
Copper steel (40%)
10-NBS
128
240
1647
16.7
High-tensile steel (HTL-85)
(0.8 oz zinc coating)
(HTL-135)
14-BWG
14-BWG
83
83
99
99
460
703
117.2
130.0
(HTL-85)
1 2-BWG
109
170
793
68.2
(HTL-135)
1 2-BWG
109
170
1213
76.5
(HTL-85) .
10-BWG
134
258
1199
45.0
Bronze TP drop
18-\WG
40
159
340
259.0
Bronze TR drop ....
18-4.WG
40
232
340
259.0
Bronze NP drop
18-4.WG
40
227
340
259.0
Hard-drawn copper HC drop.
Telegraph
Hard-drawn copper
14-AWG
9-AWG
64
114
316
208
380
644
26.4
4.3
Copper steel (40%)
6-AWG
162
384
2430
5.3
Iron
8-BWG
165
378
1090
13.3
Copper (tw. pr.)
1 6-AWG
51
208 (pr.)
500 (pr.)
104.0 (pr.)
Steel drop (sgl.)
1 6-AWG
51
104 (sgl.)
250 (sgl.)
52.0 (sgl.)
10-56
TRANSMISSION CIRCUITS
CABLE, consisting of insulated, annealed copper conductors, enclosed in a cylindrical
lead sheath, is employed in both toll and exchange telephone and in telegraph plant, where
the number of circuits required along a given route, plant economies, or interfering condi-
tions preclude the use of open wire. Cable is used generally in toll plant in urban areas
and, supplementing open wire, between principal traffic centers throughout the country,
either as toll entrance facilities for open-wire lines or as toll cable facilities directly connect-
ing large switching centers.
Telephone and telegraph cable is manufactured in various sizes and gages, of which
representative types and associated data are given in Table 3. For both types of service,
Table 3. Representative Cables — Mechanical Characteristics
Type
(3)
No. of
Pairs
(1) (2)
Gage
of Con-
ductor
Conductor
Insulation
Sheath
Thick-
ness,
in.
Outside
Diameter,
in.
Weight
per
Foot,
Ib
Type of
Core
Exchange
6
19
Paper tape
0.063
0.42
0.41
Layer
Exchange
455
19
Paper tape
0.115
2.61
8.48
Layer
Exchange - ,
11
22
Wood pulp
0.063
0.42
0.40
Layer
Exch&ngj?
909
22
Wood pulp
0.115
2.61
8.46
Multiple-^unit
Exchange - « - . r -
11
24
Wood pulp
0.061
0.36
0,31
Layer
TSxrhft,isgp
1515
24
Wood pulp
0.115
2.61
8.64
Multiple-unit
Exch&ngc . ...
11
26
Wood pulp
0.060
0.32
0.27
Layer
ExrhiAnge , . - - -
2121
26
Wood pulp
0.115
2.61
8.15
Multiple-unit
Toll entrance
(4)
12 quads
19
Paper tape
0.082
0.85
0.79
Layer
Toll entrance
i 3 quads
\ 27 ouads
13
16
Paper tape >
Paper tape >
0. 118
2.35
6.41
Layer
160 quads
19
Paper tape J
Toll (full size)
154 quads
19
Paper tape
O.T23
2.59
7.60
Layer
Notes; (I) All conductors are annealed copper.
(2) Some 28 gage exchange cable was made during World War II to conserve copper in sizes
11 to 303 pairs.
(3) The smallest and largest sizes of exchange cable are shown, as used in the Bell System.
(4) Toll entrance and toll cable may have optional groups of non-quadded exchange pairs.
The cable data given assume no shielding or sheath protection or exchange conductors.
(5) Insulation resistance required to exceed 500 megohms per mile.
(6) Some 13 gage is used in both telephone and telegraph service.
paper or wood-pulp insulated conductors are grouped together to form a core, either in
layers or 51 and 101 pair units, various colors being used in the insulation and binding
strings to permit readily distinguishing between different layers, units, quads, or pairs, for
installation or maintenance purposes. Figure 5 shows the method of core construction
for both layer and multiple-unit type cores of telephone exchange cable (24 gage-type
DSM).
Exchange conductors are generally associated in pairs (2 conductors twisted together),
although some exchange trunk cable is quadded (2 pairs twisted together as a 4-conductor
unit group, called a quad). Toll conductors are usually quadded for phantom circuit
operation, although toll cables frequently contain some non-quadded pairs for program
or other toll services. In addition, complements of exchange pairs are frequently included
in the toll cable. The lead sheath enclosing the paper-wrapped core of insulated conductors
normally contains about 1 per cent of antimony to strengthen the sheath, the thickness of
which, varies with core diameter and type of cable from about 0.06 to 0.125 in.
Cross-talk must be carefully considered in cable design, particularly for toll cables. In
non-quadded cables the conductors are twisted together in pairs. The twists in adjacent
pairs within a layer and in adjacent layers are of different lengths to provide the necessary
capacitance balance between pairs. In quadded cables the conductors are twisted together
in pairs and the pairs are twisted together with different lengths of twist to form quads
of as many as 9 types, each of which has a different length of twist. Exchange pairs (non-
quadded) are usually random spliced within their color groups (spliced without testing
t® <ie*ermiBe thB pair numbers), so that any given pair in the cable is adjacent to any other
TKANSMISSION-LINE CONSTRUCTION
10-57
pair in as few cable sections as practicable. Toll pairs, because of their greater importance,
wider range of operating energy levels and frequency assignments, are carefully spliced
where sections of cable join. The splicing is carried out according to a plan which provides
for limiting the cross-talk between circuits.
Segregation, to reduce couplings at carrier frequencies between oppositely transmitting
pairs or quads used for cable carrier, is usually accomplished by assigning oppositely bound
groups to separate cables. Segregation of pairs used for open-wire carrier is obtained by
using alternate layers or by metallic layer or unit quad shields in the same cable, as may
be required to prevent excessive cross-induction between them.
Sheath protection is provided in various degrees, as may be required, by using: (1) layers
of Sisalkraft paper and jute covering, where soil corrosion may occur; (2) layers of thermo-
plastic compound covered by longi-
tudinal copper tape, flooded with
asphalt compounds, for a lightning
shield; (3) layers of Sisalkraft paper,
two steel tapes, and jute, for gopher-
infested areas; (4) layers of Sisalkraft
paper and a layer of rubber or as-
phalt-back fabric tape for corrosion
protection in conduit; (5) a thermo-
plastic compound layer and outer
covering of impregnated fabric tape
for corrosion protection when buried
near pipe lines; (6) two helical wrap-
pings of tape armor and a cushion of
jute to protect against ring cutting,
stone bruises, or to provide shielding
for low-frequency induction for aerial
cables; and (7) single and double
armor wires with a jute cushion for _/ eoepwjRs
submarine cables. Other special
protection may be provided as re-
quired.
Spiral-four disk-insulated cable is
used, under certain conditions, to
provide entrance facilities for open-
wire carrier systems operating at a
maximum frequency of about 140
fcc. The individual units contain 4
copper conductors of 16 gage, insu-
lated from each other by composition
disks having uniformly spaced peri- ££ l&fSSSSSgcSSS <J
pheral notches which hold the wires
spaced at the corners of a square, each oppositely positioned pair of wires forming a pair
of the quad. Shielding is provided over a spiral-4 unit consisting of a copper tape and two
steel tapes. A toll entrance cable may contain up to 7 such units, each with its own metal
sheath, or a combination of units and standard paper-insulated quads and pairs which
provide other communication facilities.
Coaxial cable, of latest design, for use with the carrier and other high-frequency systems,
consists of up to 8 units. Each unit is composed of a 100.4-mil conductor (inner conductor)
positioned in the center of a single 12-mil copper tape (outer conductor) with longitudinal
seam to form a 0.375-in. (inner diameter) tube, over which are lightly wrapped two 6-mil
steel tapes. The outer conductor is supported by polyethylene disks, 0.085 in. thick,
spaced about 1 in. apart along the inner conductor. The outer and inner conductors form a
metallic circuit. With the 8 units, other standard paper-insulated quads of conductors
(up to about 78 quads of 19 gage or equivalent) may be included in the same overall lead
sheath. Further details regarding this cable and its characteristics are given in Section 17.
Both exchange and toll cables are placed aerially and underground, depending upon the
location and other factors affecting any given cable.
When cables are placed aerially on poles or towers, the required strength of the support-
ing structures must be carefully determined on the basis of loading area, exposure to
weather conditions, load carried, importance of the cable to service, and other factors such
as apply in open-wire construction. When cables are placed underground, the main factors
to consider are the type of underground housing, if any, to employ, as well as the possibili-
ties of damage from corrosion or other external sources, and the proper routing. Under-
KEY:
W-C = WHITE -GREEN
W-B = WHITE- BLUE
W-RsWHITE-RED
(?) =BLU6-RED TRACER ftMR
NOTE.
NUMBERS ARE TOTAL PAIRS IN CROUP
INCLUDING ONE TRACER BMR WHERE
INDICATED
ALL UNITS JN THE SAME LAYER HAVE
UKE COLORED BINDING STRINGS
Diagrams Showing Typical Layer and Multiple-
" ' ~ " ~ (Courtesy Bell System)
e BWRS
10-58 TRANSMISSION CIRCUITS
ground cables may be placed in vitrified clay conduit, fiber, or other types of ducts or
buried directly in a trench in the ground or plowed into the ground. In any event, suitable
protection from underground hazards must be provided.
Loading coils are provided in cable circuits (aerial or underground) wherever required
for transmission reasons (see Section 17).
Loading coils are generally assembled in groups in steel cases for either aerial or under-
ground installations, and some designs are suitable for office relay rack mounting. Lead
sleeve cases are used for loading small complements of toll and exchange conductors. Also
single coils (in a small metal case) are designed to be connected and enclosed in cable
splices.
UNDERGROUND STRUCTURES, consisting of conduit, manholes, vaults, and other
construction, are designed to provide suitable housings for underground cable plant. These
structures are a necessity in cities and to some extent in the smaller communities (assuming
that aerial cable plant is not practicable or economical in a given case) , since the under-
ground cable plant must be readily accessible to permit additions, changes, removals, and
repairs. Some underground exchange cable has been buried (placed directly in the ground)
in built-up locations, but this is not the general practice. Toll cables, suitably protected,
are frequently plowed into the ground or are buried in trenches. This type of construction
has been employed for long distances over transcontinental and other important toll cable
routes.
Underground conduit may be of vitrified clay, fiber composition, creosoted wood, or
iron pipes. Clay conduit is most generally employed for main routes because of its rela-
tively low cost and satisfactory performance when buried and properly protected. It is
manufactured in single or 2-, 3-, 4-, 6-, 8-, and 9-duct multiple units, and is usually laid
in one or more units in a compact arrangement. The conduit is placed in a trench, which
may vary in depth to avoid other underground structures or hazards (sharp changes in
direction are avoided), on a solid base with or without concrete. It may be encased com-
pletely in concrete or only at the top or bottom, or plank may be used, in the judgment of
the engineer as to the type of construction needed.
Conduit may be placed along a street under paving or the sidewalk, or between the curb
and sidewalk, or in parking in the center of the street, as conditions permit. Costs and a
satisfactory permanent location, least likely to be disturbed, are primary considerations
in placing conduit over a selected route. Subsidiary ducts of wood and of vitrified clay,
sewer or iron pipe are commonly used from manholes to underground cable poles or build-
ings.
Manholes are required at junction points of conduit runs and other locations where it
is desirable that the underground cable plant be made accessible, and to provide for
practicable cable section lengths. Manholes are preferably located at one side or the other
of street intersections to avoid interfering with traffic, when working in them. Manholes
vary in size from the small service boxes, placed mainly for the purpose of pulling cable,
to the standard 2-, 3-, and 4-way and center rack types, having dimensions ranging from
3 ft 6 in. width by 6 ft length by 5 ft 6 in. headroom to 8 ft width by 9 ft length by about
6 ft or more headroom. In addition, special type manholes and cable vaults of various
sizes are required in many cases to accommodate concentrated conduit entrances, as at
central offices and loading coil installations. Concrete construction is usually employed,
with or without reinforcement. Manhole frames and covers of cast iron, placed in the
manhole roof to provide a suitable entrance of 27-in. diameter or more to the manhole,
are designed to support surface traffic safely. Drainage may or may not be provided in
manholes, as required.
The underground cables are supported on galvanized-metal racks, mounted vertically
along the sides or through the center of the manhole, and are separated by a few inches to
permit splices to be made and opened as required.
26. ELECTRICAL PROTECTION OF TRANSMISSION LINES
Lightning and power circuits are two unlike sources of electrical power, which, under
certain conditions of exposure or contact encountered in practice, occasionally cause dam-
age to communication plant.
Communication lines and equipment are necessarily grouped closely together because
of space limitations and other economic considerations. These facilities will carry their
normal operating voltages and currents with ample margins of safety, but the insulation
employed on cable conductors, between conductors and the cable sheath, and in various
equipments is not sufficient, in general, to withstand lightning or power circuit potentials
witliout protection.
\
ELECTRICAL PROTECTION OF TRANSMISSION LINES 10-59
EXCHANGE CABLE PROTECTION against lightning for any given exchange cable
plant usually requires a study of the plant layout and exposure conditions involved. The
aerial cable sheath is usually grounded through the underground cable plant or at the cen-
tral office and at various other locations at irregular intervals, such as at underground dips
or private cable entrances.
The working cable conductors are grounded by operation of the station protection and
through the loops connecting to them. Cable conductors may serve subscriber stations
at one or more intermediate points along the conductors but lie idle in other sections of
the cable beyond these points. Other conductors may lie idle throughout their length,
and groups of conductors will terminate at various
points where cable sizes change. All these conditions
have a direct bearing on potentials in exchange cables
due to lightning.
Lightning currents may, in general, be impressed on
exchange cables by (1) inductive coupling between the
cables (or between conductors connected to them) and
the lightning path, (2) direct stroke, or (3) metallic con-
nection with entering open-wire or drop loops, carrying
lightning potentials, as a result of a direct stroke or
other causes. Lightning currents from metallic connec-
tions (by conduction) are usually the principal con-
sideration in the design of exchange cable protection.
Lightning current may appear on the open wire, con-
nected to the cable, from such sources as direct strokes
to the line, conduction from service drops or guys, or
from arcs from power-system ground wires. Figure 6
shows the results of crest current measurements at ex-
change cable-open wire junctions.
Although lightning currents reach cables over both connected drop and open-wire loops,
it appears that the currents on the drop loops will probably be greater than those on the
open wire. However, cable plant with drop loops is generally located in built-up areas
having low-resistance public water systems and various types of shielding, whereas open-
wire plant extends mostly into rural areas where direct lightning strokes are more likely
to occur and where grounding conditions are not as favorable as in built-up areas. Thus,
cable damage from lightning currents is more likely to result from open-wire than from drop
loops. In some locations where cables extend into rural districts and are subject to the
same lightning exposure as the open wire the current received by the cable from the drop
loops may be of greater importance than that re-
ceived from the open-wire loops connected to these
cables.
Lightning currents, reaching exchange cable from
any source, produce potential differences between
conductors and between the sheath and conductors
which, if protection is not provided, may seriously
damage the sheath and the enclosed conductors.
The potential differences within the cable, result-
ing from current on the conductors, depend largely
on the current wave form. For steep wave-front
surges, the relatively high self and mutual surge
impedances are important in determining the poten-
tial differences; for slower surges or short cables
(about 1 to 2 miles) these potential differences
depend more upon the conductor resistances. Fre-
quently, the slower surges produce the lower poten-
tial differences. Figure 7 illustrates the voltage dis-
O 20 4O 6O 8O JOO
PER CENT OF CUfWEMT EXC££DiN«
ORDi NATES
FIG. 6. Crest Current Distribution
for Lightning Currents at Exchange
Cable — Open Wire Junctions (Cour-
tesy Bell System)
•US. CABLE ••* AERIAL CABLE
ET
wx/wwiw/a SHEATH _
i
CONDUCTOR GROUPS:
1. CONNECTED TO WJRE
2. SPARE
3.WOftKJNft AT X
\
FIG. 7.
DISTANCE ALONG CABLE
Voltage Distribution
^ _^. _w i_j_ along
Conductors andlSheath for Current De-
livered from Open Wire — No Protector
Blocks on Conductors (Courtesy Bell
System)
tribution along conductors and sheath for current delivered from an open-wire loop with
no protector blocks at the junction of the open wire and cable. The aerial cable is not
grounded, except through the underground section and the office ground, and contains a
group of conductors (1) connected to open-wire loops, (2) spare, and (3) working at an,
intermediate point, x, along the cable.
Potential differences in cables, unless several times the breakdown voltage of tne cable
insulation, do not, in general, cause permanent damage, although the insulation may be
punctured in numerous places. Remedial measures are, therefore, designed to reduce the
applied voltages between conductors and between conductors and the sheath and to limit
or distribute the current so that permanent failures are unlikely even though punctures
10-60
TRANSMISSION CIRCUITS
do occur. Such measures may consist of (1) connecting protector blocks between conduc-
tors and sheath where potential differences are most likely to be high and occur frequently,
(2) providing means of diverting from the cable a substantial part of the current which
might reach the cable over open-wire or drop loops serving installations exposed to lightning
strokes, such as radio and fire towers, and (3) placing conductors parallel with the sheath,
thus increasing the conductivity and reducing the IR drop along the sheath.
Protector Blocks. One type of protector block, commonly employed between cable
conductors and the enclosing sheath at the junction of open-wire or drop loops and cables,
consists of a porcelain block with a small carbon block insert held in place by a quick-
melting glass cement. The porcelain block is held against a solid carbon block (which
rests against a grounded metal plate) by a metal spring bearing against the small carbon
insert. The insert is positioned to provide an air gap between it and the grounded carbon
block of about 0.006 in. One set of these blocks is provided for each of the two conductors
of the cable pair. When the current in the air gap is sufficient to melt the cement, the
metal spring, which is connected to a cable conductor, forces the carbon block insert
against the ground block, thus grounding the loop wire and cable conductor to which the
loop wire is connected.
These protector blocks break down when steep wave front voltages of 1000 to 1500 volts
are impressed, this voltage range being generally somewhat below the steep wave front
voltage necessary to puncture exchange cable insulation. Protection is thus provided for
the cable conductors, having protector blocks, against dielectric failure near to the point
where these blocks are connected. However, damaging potential differences may occur
between the protected conductors and other conductors at the point of protection and be-
tween conductors and sheath at other points. Lower-breakdown protector blocks for
cable protection do not appear to offer an important improvement in protection and
generally react unfavorably from the standpoint of maintenance and service.
Protector blocks applied to working conductors at the junction of open-wire and aerial
cables (not grounded at intermediate points) reduce potential differences between such
conductors and the sheath and other conductors, as
shown by a comparison of Figs. 7 and 8. The curves
in these figures are not drawn to scale, and actually
the reductions obtained are much larger than can be
indicated conveniently. With working conductors
thus protected (Fig. 8), the maximum potential differ-
ence within the cable usually occurs at the open-wire
junction between the sheath and spare pairs, and the
next highest potential difference appears at the junc-
tion of the aerial and underground cable between the
sheath and protected conductors.
When protector blocks are applied to all conductors
at the junction of open-wire and aerial cables, the
potential differences between conductors are elixni-
Fro. 8. Voltage Distribution along nated throughout the cable (assuming an ideal con-
SSS^S^S? Wir^ototo tit™ of no Sounds on the conductors through station
Block on Conductors Connected to blocks at other points) . The only potential difference
Wire (Courtesy Bell System) existing in the cable under this condition is between
the sheath and all conductors, being a maximum at
the junction of the aerial and underground cable sections and about equal to the IR drop
on the conductors through the underground section.
Protector blocks (usually with 10-mil air gaps) for all wires may also be placed along
the open-wire line, as required, to divert current from the cable. This results in increased
effectiveness for a given ground impedance, due to increasing the impedance between the
ground point and the underground cable, over what it would be for a single sheath ground
at the open-wire junction, and it avoids the adverse effects of a single ground on the sheath.
Experience indicates that improvements usually result when the open-wire protection is
placed within about 700 to 3000 ft of the cable terminal and the ground resistance at the
protection does not exceed about 30 ohms.
Grotmds may consist of several hundred feet of buried wire in high-resistivity areas, or
rods may be used effectively in low-resistivity areas. Grounds of limited extent have
impedances about equal to their d-c resistances, but for lengths of wire or pipe greater
than about 200 ft the d-c resistance decreases with length faster than the impedance.
Figure 9 shows, for homogeneous earth, the variation of resistance with length of buried
wire, the earth resistivity being 100 meter ohms. Large variations may be expected in
tlieae values where the soil has a highly variable resistivity. For grounds of equal d-c
resistances, the ground of least extent is considered best for grounding purposes; although,
CONDUCTOR SROOPS:
J. CONNECTED TO WWE
DISTANCE ALONC CABLE
ELECTRICAL PROTECTION OF TRANSMISSION LINES 10-61
*PG* WO METER-OHMS EARTH RESISTIVITY
25 50 75 tOO 300 50O TOO 900
LENGTH OF WIRE IN FEET
FIG. 9. Approximate Resistance to
Ground of a Buried Wire (Courtesy
Bell System)
practically, the neutral of a well-grounded common neutral power system or water piping
system, if available, will probably provide a better ground than a made ground.
Shielding conductors placed on the pole line along with the cable or buried below it
will reduce conductor-to-conductor and sheath-to-conductor potentials by about 50 per
cent or more. The effectiveness of shielding depends upon diverting part of the current
from the sheath. This method of current diversion has been limited because more prac-
ticable methods are available.
Increasing sheath conductivity by placing bare conductors along the sheath and in
contact with it will reduce the IR drop along the
sheath and potential differences within the cable.
Other remedial measures include:
(a) Increasing core to sheath dielectric strength.
This method is of major importance in toll cables,
where the voltages between core and sheath appear
most frequently, but for exchange cable, where the
voltages between conductors are of more concern, this
method is of lesser importance.
(6) Employing pole protection wires on exchange •§ &
cables extending into rural areas where cable terminals
are infrequent.
(c) Bonding to power system common neutrals at
frequent intervals in built-up areas where many work-
ing drops are connected through protector blocks to
the cable sheath. In such cases, the cable sheath be-
comes closely tied in with the neutral through the drops, station protector grounds, and
power secondary services. By proper bonding (at about ^-mile intervals or less) between
sheath and neutral (assuming the neutral to be continuous and well grounded), the neutral
forms a parallel path with the cable for lightning currents and provides effective shielding.
Under such conditions, cable damage from power contacts or lightning tends to be re-
stricted to a section between the two bonds immediately adjacent to the power source.
Bonding to the neutral also lowers the sheath impedance and thus assists in prompt
de-energization of the power circuit in the event of power-circuit contact with the sheath.
Frequent bonding to the neutral is useful for cable noise mitigation.
Where bonding between the aerial cable and power neutral is objectionable, with respect
to corrosion on the associated underground cable plant (as where drainage is used), the
bonded aerial sheath may be isolated from the underground sheath by installing an insulat-
ing joint at their junction, reliance being placed in the bonding for the aerial sheath pro-
tective grounding.
Experience indicates that it is advisable, in lightning affected areas, to protect all work-
ing conductors at any terminal, serving any open wire or drop loop over 1/2 mile in length,
this length being based principally on judgment.
Some companies (not Bell System) employ, in some cases, fuses (usually 5- or 7-amp
rating) in conjunction with protector blocks to form a unit-type protector which is usually
assembled in multiples and mounted in a terminal housing for installation at the junction
•of open-wire or drop loops and the cable. The protector blocks ground the open-wire or
drop loop when lightning or excessive power circuit
potentials are applied, and the fuses open the circuit
when the current coming into the cable over the loop
exceeds the fuse rating.
TOLL CABLE PROTECTION (against lightning)
requirements are similar to those of the exchange
plant except that the distances are greater, partd<m-
larly between grounds. Experience indicates that
the rate of lightning troubles on aerial tott cables
apparently does not differ greatly from such troubles
in buried cables, but the ease of locating and clearing
these troubles in aerial cables as compared to under-
ground cables indicates less need for comparable
remedial measures on the aerial cables.
Figure 10 shows the distribution of lightning
stroke crest currents, based on a large number of
measurements in the ground structures of power-
transmission lines, the crest value varying over a wide range. Measurements indicate
that the crest valite is reached in 5 to 10 microseconds and that it decays to half its maxi-
.mum value in 25 to 100 microseconds. The crest value and decay time to half value of the
KX)
50
4O
3O
\
^x.
""^
^
^v
*s
^
\
10
5
Y
^
2345 1O 203O50 TOO
PER CENT OF STROKES WHTH CURRENTS
EXCEEDING ORDiNATE
FIG. 10. Distribution of Lightning
Stroke Crest Currents (Courtesy Bell
System)
10-62
TRANSMISSION CIRCUITS
current, rather than wave front steepness, are of primary importance with respect to
voltages between the sheath and conductors of aerial or buried toll cable.
At a point remote from ground connections, the surge impedance to ground of an aerial
cable sheath (any size) is about 200 ohms (400 ohms in each direction from the lightning
stroke) . For a crest current of 20,000 amp the sheath-to-ground voltage would be 4 million
volts. The conductors within the sheath attain about the same potential to ground as
the sheath, owing to capacitive and inductive coupling between the sheath and core con-
ductors. However, some voltage difference does exist between the sheath and core, due
to the IR drop along the sheath, resulting from the flow of lightning current on the sheath.
This voltage difference is greatest at the stroke point, decreasing as the distance from the
stroke point increases. The higher the sheath resistance, the greater this voltage difference
between sheath and core will be for a given lightning current.
The dielectric strength between core and sheath, for normal-dielectric-strength cables,
is for surges about 2000 volts. For high-dielectric-strength cables (having an extra core
wrap), a 4000- volt value for surges may be assumed.
After an initial puncture in the insulation near the stroke point, other punctures will
thus usually occur some distance away in either or both directions. Such puncturing may
or may not cause permanent failures, depending on the current through the fault.
A sheath-to-core voltage of breakdown magnitude may develop, owing to: (1) a large
sheath current for a relatively short distance, (2) a smaller sheath current over a longer
distance, or (3) a combination of (1) and (2), depending on the ground paths from the
sheath and their locations with respect to the lightning stroke. Permanent damage is
likely to result from the large current transfer through the punctures in condition (1)
but is not so likely in (2) because of the smaller transfer of current from sheath to con-
ductors under this condition.
The voltages in buried cables are usually due to large sheath currents over short distances
(less than x/2 mile), so that permanent damage is likely at puncture points.
The protection of aerial toll cables may consist of (1) pole protection wires (wires bonded
to the sheath and extending down the pole to the pole butt or to a point near the ground
line), (2) aerial shield wires, (3) buried shield wires, (4) high-dielectric-strength cable (with
double core wrap), (5) shields within the cable, or (6) protector blocks at open-wire junc-
tions or out from the junction about a mile on the open wire.
Pole protection wires may serve not only to protect poles against splintering but also
to provide protection to aerial cables in lightning exposures. Data show that for such
wires, properly spaced along an aerial cable line, the voltage between sheath and core, due
to a stroke, decreases as the number of such wires increases up to about 10 for 100 meter
ohm resistivity and up to about 20 for 1000 ohm resistivity. However, in uniform ex-
posures,-"the effectiveness of these wires decreases for aerial cables having both toll and
exchange conductors as the interval (of the order of
1 mile) between subscriber drop locations decreases,
owing to the low-breakdown path from sheath to
ground over the drop loops which substantially short-
circuits the pole protection wires.
The effectiveness of these wires may be lowered
where a large number of them are employed, as the
result of current distribution along the sheath to such
grounds from the stroke point increasing the net
sheath-to-eore voltage. By using proper length gaps
in the wires, the number of conducting grounds may
be limited to an optimum value.
Where pole protection wires are not adequate to
give required lightning protection to aerial cables,
1.8 2.2
CABLE DIAMETER Bsl *NCH£$
^ ** aerial or buried shield wires may be of advantage.
oi.- u -D .L r * • i The reduction in core-to-sheath voltage by aerial
Shield Factors for Aerial , . , , . , . , i_j.j ^ A1_ .i^tAx _u
FIG. II.
Shield Wires (Courtesy Bell System)
shield wires which are bonded to the sheath at each
pole is normally substantial, as shown by the shield
factors, Fig. 11. When an aerial cable is provided with buried shield wires, the voltage
from a direct stroke is about the same as that for a buried cable of the same size with
similar shield wires.
High-dielectric-strength cables should generally be employed in new installations. The
choice of this type of cable may obviate the necessity of other remedial measures, but in
any event its higher dielectric strength is an advantage since, if the strength is doubled,
the stroke current must be increased 3 times to puncture the insulation.
Communication plant may be damaged by contact with high-voltage wires or power
distribution circuits. The most important consideration in protecting cables from power-
CABLE SHEATH CORROSION 10-63
wire contact is to so locate, construct, and maintain the communication, and power circuit
plant that contacts will not occur.
Aerial cables are grounded at offices, through their connection to the underground cable
plant, underground dips, and private cable entrances, as well as other frequent grounding,
such as, in some cases, to multigrounded power circuit neutrals. This practice contributes
to provide a low-impedance ground to de-energize the power circuit promptly in case of
contact with the cable plant.
27. CABLE SHEATH CORROSION
ELECTROLYSIS. Electric currents, flowing in the earth, may result from (1) stray
currents from d-c street-car (trolley) or electrified railway systems, (2) stray currents from
commercial d-c power distribution systems, (3) differences in the chemical composition of
films on the cable sheath at different locations, (4) differences between the composition
of films on sheaths of different cables at the same location, (5) differences in the electrolyte
at different places, or (6) a number of other conditions. These currents passing through
damp ground cause chemical changes to take place at electrode surfaces, such as cable
sheaths, which may or may not affect the electrodes.
Cable sheath corrosion may, in general, be considered as occurring in:
1. Stray-current areas.
2. Non-stray-current areas.
The principal causes of cable sheath corrosion are:
1. Stray current-anodic action.
2. Stray current-cathodic action.
3. Localized action.
4. Galvanic action.
5. Chemical attack.
Stray-current areas are commonly designated as those in which the cable-to-earth
potentials and sheath currents are established principally by currents straying from the
rails of d-c transportation systems and utilizing other paralleling paths of relatively low
resistance in the earth, such as cable sheath or public water piping.
Where the stray current enters the sheath the cable is negative (cathodic) to the earthr
and where it leaves the sheath the cable is positive (anodic) to the earth.
Non-stray-current areas are those in which corrosion may occur from other than
stray currents. Currents in these areas usually result from potential gradients due to
such causes as differential aeration, differential electrolyte concentrations, non-uniformi-
ties in the sheath metal, or potential differences between different metals.
Current from stray-current areas may flow in non-stray areas, such as along an under-
ground toll cable sheath extending between cities where street cars operate. Current,
usually considered as "non-stray" current, such as that resulting from galvanic potentials,
may also be present in stray-current areas, although its effect is largely overshadowed by
the stray currents in these areas.
Anodic corrosion, due to stray currents, results because:
1. The metal becomes positively ionized and goes into solution.
Pb - 2e -> Pb++ (e = electron)
2. The anions (ions bearing negative charges and migrating to an anode) in the elec-
trolyte are attracted to and contact the sheath, where they lose their charge, become
chemically active, and attack the lead sheath.
If the ions are chlorine
Cl- - e -> Cl
and
Pb + 2C1 -» PbCl2 (lead chloride)
Note: A positive ion, in the case of Pb4""*", is an atom from which two electrons have been removed;
a negative ion, in the case of Cl"", is an atom to which one extra electron has been added.
In anodic action, a corrosion product does not always adhere to the sheath, and a clean
corroded area on the sheath is regarded as due to such action. The corrosion product, if
present on the sheath, is usually lead chloride or lead sulfate or both. The sheath poten-
tial, being positive, attracts chloride and sulfate ions in the ground water to the sheath,
and these ions react with the lead. Under severe anodic conditions lead peroxide, PbOa,
may be formed. This product has a chocolate color; the products of chloride, sulfate, and
carbonate of lead are white.
10-64 TRANSMISSION CIRCUITS
Cathodic corrosion, due to stray currents, though not as yet reproduced in the laboratory,
might possibly occur when the cables are negative to earth and the surrounding earth
contains alkali or salts of sodium, potassium, calcium, or magnesium. Hydrogen ions in
the electrolyte, under such conditions, are attracted to the sheath, lose their charge, and
are liberated, resulting in a decrease in hydrogen-ion concentration and making the elec-
trolyte alkaline. The alkali forms most rapidly and with greatest concentration at points
of maximum cathodic current density. The attack on the sheath is, therefore, not uniform
and usually affects only a relatively small part of the sheath.
La the case of sodium salts, the reaction with the lead is:
H+ -f e -+ H
Na+ + OH~ — > NaOH (sodium hydroxide)
The sodium hydroxide forming at the sheath dissolves the lead, and the final reaction
usually results in the formation principally of lead monoxide, PbOT lead carbonate, and
sodium carbonate. The sheath pitting may be similar to that caused by anodic action,
but the cathodic corrosion is characterized by the usually bright orange-red color of the
lead monoxide.
Galvanic action usually results when two dissimilar metals are in electric contact with
an electrolyte and also are metallically connected. Where cables and bare copper or gal-
vanized cable rack supports are present in a flooded manhole, galvanic action may occur.
Lead is anodic to copper and cathodic to the zinc galvanizing, the anode corroding in each
case. Corrosion may appear, in the presence of moisture, on wiped joints and soldered
seams on cable sleeves, where the solder may be anodic to the lead.
When two dissimilar metals in an electrolyte are connected metallically, the metal with
the higher solution pressure becomes the anode and corrodes. Current passes from the
anode through the electrolyte to the cathode and completes the circuit to the anode through
the metallic connection.
In alkaline solutions, lead tends to become electronegative and may be anodic with
respect to another metal such as iron. Thus, lead corrosion may result where cable is
installed in iron conduit and such solutions are present. Under these conditions current
may pass from the lead through the solution to the iron and return to the lead at points
of metallic contact between the iron conduit and the sheath.
Local action between adjacent areas of the sheath may result from variations in sheath
material, such as foreign particles in the lead, and from differences in surface conditions
due to abrasion. Corrosion from the action, under anodic conditions, may occur in spots
rather than uniformly over the sheath surface, and if the action continues for a period of
years sharply defined pits may appear in the sheath.
Concentration cells may be formed by a change in the concentration of the salts in an
electrolyte, causing corresponding changes in the potential of a given electrode in contact
with the electrolyte; or by two electrolytes, with equal concentration of different salts,
producing different electrode potentials on the same metal. Such a cell might be established
by waste products from a factory or sewer entering a sloping conduit (with cable) at a
conduit joint and concentrating along a section of sheath. The cell might then result be-
tween the section of sheath having the concentration and an adjacent section not affected
by the waste.
Differential aeration, which may be considered a special form of concentration cell,
results in sheath corrosion, owing to a variation in the concentration of dissolved oxygen
in the electrolyte in contact with the sheath. Where a sheath is continually wet by water
dripping or condensing on it, there will be more oxygen in the moisture exposed to the air
than where the moisture is shielded by an absorbent material such as a layer of silt on the
sheath. The cable sheath in contact with the electrolyte with a deficiency of oxygen will
be anodic and subject to corrosion.
Battery action in the soil might result in sheath corrosion where the sheath was not one
of the cell electrodes but acted as a conductor of the local current. As an example, if an
iron pipe passed through a bed of cinders which acted as a carbon electrode, and the
adjacent section of pipe was in contact with ordinary soil, a cell would be established with
the carbon electrode negative to the adjacent section of pipe. Part of the resulting current
from this section might enter a nearby paralleling cable sheath and leave the sheath near
tEe cinders, at which point sheath corrosion might result.
Protective films formed over the sheath by natural processes are usually helpful in pre-
venting sheath corrosion. Films formed from silicates are generally continuous, adherent,
insoluble, and helpful, whereas films resulting from nitrates in the soil tend to prevent film
aid corrosion.
CABLE SHEATH CORROSION 10-65
REMEDIAL MEASURES for controlling corrosion are varied and often complex, be-
cause the problems of corrosion may differ over a wide range of causes and conditions and
extend over relatively large areas.
Generally, the first considerations in the control of cable sheath corrosion are electrical,
involving a thorough study of electrical conditions affecting the cable plant. Chemical
control can sometimes be used successfully where electrical methods are not practicable.
The general attack on sheath corrosion problems by electrical methods consists of:
1. Limiting current entering the sheath to the extent practicable.
2. Providing metallic paths by which current entering the sheath may leave it without
damage to the sheath or other metallic structures.
Protective arrangements of any nature should be such as to minimize the probability
of impressing current on other underground plants, either privately or publicly owned.
The limitation of current pick-up by a given underground cable sheath requires that the
sheath be kept free of all connections to other grounded metallic structures except those
connections specified as part of the general remedial plan, and that the sheath should not
be made more negative to earth in any area than is necessary under practical design.
The cable sheath should be maintained at slight negative potential to earth to (1) limit
current pick-up which increases with increase in negative potential, (2) lessen the possi-
bility of large positive pipe-to-cable voltages, and (3) reduce the chances for cathodic
corrosion.
The increasing use of bonding between aerial cables and multigrounded power neutrals
for noise induction and protection reasons increases the tendency to discharge current to
the underground cable plant. Insulating joints may be used at underground-aerial cable
junctions, where required, and electrolytic capacitors may be employed to bridge the
insulating joint if capacitors are necessary for noise induction or protection purposes.
Cathodic corrosion of sheaths may occur where the cable-to-earth potential exceeds a
few tenths of a volt negative. In the presence of salts this potential may not be over 0.2
volt; under other conditions cathodic corrosion will not result at any potentials encoun-
tered, where an effective drainage system exists.
For this type of corrosion, it is essential to maintain low negative cable-to-earth poten-
tials by using (1) an adequate drainage system, (2) insulating joints shunted by resistors
if necessary, (3) corrosion-protected cables for replacement of cables which fail, (4) periodic
flushing of ducts which accumulate alkali, or (5) reverse drainage employing controlled
currents to the cables by connecting to positive points on rail systems or to pipes (expe-
rience limited).
Other underground structures, such as public water or gas piping, are also drained in
many areas. A metallic piping system in direct contact with the earth usually has a very
low leakage resistance, and any reduction in its potential by drainage tends to lower the
earth potential in its immediate vicinity. Where the earth potential is thus lowered, the
current discharge from nearby telephone cables tends to increase. This condition may
complicate the telephone cable drainage scheme, but generally, owing to the low leakage
resistance of the piping system, the adverse effects are not extensive. A coordinated
drainage plan for all underground systems is usually necessary where two or more systems
serve the same general area affected by stray currents.
Anodic corrosion, which is the only type of corrosion that has been found so far in non-
stray areas, results from current leaving the cable sheath for any reason. This type of
corrosion may be due to: (1) currents flowing from the cable into the electrolyte in the
duct and back to the cable without leaving the duct, as a result of differential aeration,
differential electrolyte concentration, or non-uniformity of the sheath composition (though
this type of corrosion is local, many such local cells may exist along a cable and cause
corrosion over a long section of the cable) ; and (2) currents flowing from the cable to the
electrolyte in the duet, thence to the earth outside of the duct, and finally returning to the
cable at some relatively remote point. In (2) the driving electromotive forces may result
from the same causes as given in (1) above, but the cells are materially lengthened and
the currents are known as long ceU currents. Such electromotive forces may result from
potential gradients in the earth due to currents associated with corrosion cells on long
paralleling piping or to other natural causes, including magnetic storms; or they may
result from a potential established as a result of sheath contact with other metal, such as
copper or iron piping; or they may result from remote railway currents flowing into the
non-stray area.
TESTING METHODS AND MITIGATIVE MEASURES, as employed in non-stray-
current areas, areT in general, somewhat similar to those employed in stray-ctirrent areas,
but various testing refinements are usually required in the non-stray areas. For example,
in determining the IR drop or direction of current flow in the earth as it may affect under-
10-66 TRANSMISSION CIRCUITS
ground cable sheath, it is necessary to employ electrodes, for contacting the earth, which
are identical in potential or differ by a known and constant potential. Such an electrode,
designated a half-cell, consists of a non-conducting container enclosing a metallic electrode
suspended in an electrolyte. The electrolyte fills a porous cap, which forms the bottom
of the container and through which the cell makes contact with the earth. This cell makes
use of the fact that the potential difference between electrolytes varies over a very small
range as compared to the potential difference between metals when used as electrodes.
Experience has shown that corrosion is not usually a problem with respect to buried
jute-protected, tape-armored, and thermoplastic-covered cables in non-stray areas.
Electrical tests on such cables in non-stray areas are not, in general, considered necessary.
Forced drainage has been successfully employed in anodic areas in the protection of
underground cable plant in non-stray areas. Random contacts between telephone cables
and other metallic structures, such as water piping and steel buildings, usually interfere
with effective drainage of the cables and should be eliminated, although other considera-
tions, particularly noise induction and protection, may impose numerous difficulties and
problems in such eliminations.
Forced drainage requires a separate d-c source of potential, such as a rectifier (commonly
used) or a battery, with the negative terminal connected to the cable sheath and the posi-
tive terminal connected to a negative bus or special ground. Current is forced from the
sheath to the bus or ground.
Rectifiers available for drainage purposes have suitable d-c voltage and current outputs
and usually operate from either 115- or 230-volt a-c commercial supply. They are made
in several types, including dry-disk and tube types, by a number of electrical equipment
manufacturers.
Galvanic anodes requiring no external pwer supply may provide the required amount
of forced drainage under favorable conditions when buried in the ground and connected
to the sheath by copper wire. The anodes may consist of a metal negative to lead, such as
zinc, aluminum, or magnesium. Magnesium appears favorable, because of its relatively
high negative potential (about 1 volt) to lead. The anode, being buried in the soil and
discharging current, will gradually be consumed.
To be effective, the anode must have a low resistance to ground, and this depends on its
shape and the surrounding earth resistivity. For a cylinder 4 in. in diameter by 20 in.
long, the resistance to ground (without special environment) is about equal to the earth
resistivity in meter ohms.
Chemical attack usually requires an analysis of the corrosion products and a determina-
tion of the source of the chemical attacking the cable sheath in order to apply suitable
remedial measures. Chemists may be of assistance, in difficult cases, in determining the
nature of the attacking chemicals. Lead monoxide corrosion is indicative of cathodic action
or alkali attack. Very few cases show a definite single cause of corrosion. The previous
history of corrosion of the affected cable may be of value in arriving at the causes of the
corrosion.
Alternating current, principally because of its rapid and equal reversals of potential
between positive and negative values, is not considered an important cause of cable sheath
corrosion.
Corrosion-protected cable for installation in underground conduit can be made available
with the same core make-up as the plain lead-covered cable with which it may be asso-
ciated. This protected cable may be useful where the lead sheath would be subject to
corrosive action without the protection and where it is more attractive than other remedial
measures. This type of cable may be employed in situations such as (1) near chemical
plants or other locations where chemical attack has been experienced or may occur, (2)
where alkaline attack (cathodic action) might develop, or (3) where corrosion has occurred
in subsurface dips.
One type of protection consists of two reversed layers of Sisalkraft paper and an outer
layer of rubber-filled tape, the sheath and each layer being flooded with an asphalt com-
pound. A non-adhesive coating is applied on the outside covering to prevent sticking in
handling. The protection increases the cable diameter about 0.2 in,
Suitable alarms and pilot wires to a centralized maintenance center may be employed,
when facilities are available and as required, to indicate critical changes in potentials and
current flow affecting the cable plant.
FOREIGN WIRE RELATIONS 10-67
COORDINATION OF COMMUNICATION
AND POWER SYSTEMS
By John D. Taylor and Howard L. Davis, Jr.
28. FOREIGN WIRE RELATIONS
In order to insure safety to persons and property, economy of operation, and good
service, in areas served by both overhead communication and power systems, it became
evident, as the systems began to expand, that the companies involved should establish
and follow a plan of cooperation in the construction and operation of their respective
plants. For a number of years individual cooperative efforts were carried on, but the spe-
cific solutions of the problems that developed were not applicable in a general way.
Early in 1921 steps were taken by both interests on a nationwide scale to formulate a
basis of common understanding and to establish permanent joint committees and sub-
committees for study and recommendations relating to mutual problems. As a result of
continuous study and research by these subcommittees and sponsors, the Joint General
Committee of the Edison Electric Institute and Bell Telephone System prepared, and the
representative interests approved, several general reports, of which the following are the
principal ones in effect today:
1. Principles and Practices for the Inductive Coordination of Supply and Communication
Systems, Dec. 9, 1922.*
2. Principles and Practices for the Joint Use of Wood Poles by Supply and Communication
Companies, Feb. 15, 1926.*
3. Inductive Coordination — Allocation of Costs between Supply and Communication
Companies, Oct. 15, 1926.*
In general, the Principles and Practices provide, in addition to other important items,
that
(a) All supply and communication circuits with their associated apparatus should be
located, constructed, operated, and maintained in conformity with general coordinated
methods based on the concept of rendering either service without interference.
(6) Where general coordinated methods will be insufficient, suitable specific coordinated
methods should be applied, most conveniently and economically, to prevent interference
with either service, present and known future factors being taken into account.
(c) The companies serving any given area should fully cooperate with each other in
carrying out the accepted principles, based on arriving at the best engineering solution of
each situation, as it arises, for all the companies involved.
(d) Where conditions and the nature of the supply and communication circuits permit,
joint use of poles (particularly in urban areas) is generally preferable to separate lines,
when justified by considerations of safety, economy, and convenience, and assuming that a
satisfactory agreement is reached between the parties concerned.
(e} When supply and communication facilities occupy the same section of highway and
joint use is not desirable, each type of facility should be confined to one side of the high-
way, as far as practicable, thus avoiding unnecessary crossings and expensive guying.
(/) In the design, construction, and operation of supply and communication circuits
and equipment, all factors contributing to inductive influence, inductive couplings, or
inductive susceptiveness under normal or abnormal operating conditions should be limited
to the extent necessary and practicable.
(g) Each utility shall be the judge of the quality and requirements of its own service
and the type and design of its own facilities.
(h) Coordination costs in any given situation of proximity, assuming that satisfactory
results have been attained under the best engineering solution, will generally be allocated,
so that each company involved bears its equitable portion, including its own betterments.
The basis for cooperation, as set forth in detail in the Principles and Practices, has con-
tributed immeasurably to the excellent foreign wire relations existing among the many
•wire-using companies who supply electric and communication services throughout the
country.
The cooperative plan was later extended to provide for a Joint General Committee of
the American Railway Association (now Association of American Railroads) and Bell
Telephone System in 1929, a Joint General Committee of the Edison Electric Institute
* These reports are now combined as Reports of Joint General Committee of Edison Electric Institute
and Bell Telephone System on Physical Relations between Electrical Supply and Communication Systems,
reissued July 1945.
10-68 TRANSMISSION CIRCUITS
and Western Union Telegraph Company in 1935, and a Joint General Committee of the
Association of American Railroads and Edison Electric Institute.
When power and communication facilities serve the same areas and are supported on
overhead structures and where the two types of facilities are in close physical relation or
inductively coupled or both, situations of proximity generally are unavoidable. Communi-
cation facilities, operating at relatively low voltages and currents, are not designed to
withstand the normal or abnormal power circuit voltages and currents which may be
impressed upon them by direct contact or, in severe influences or couplings, by induction.
In some cases of contact or induction, the service may be only interrupted or degraded,
but in more severe situations the service may be interrupted and the facilities damaged
with or without personnel hazard.
It is thus imperative that the Principles and Practices be closely adhered to, in order
that both services may be furnished the public in a safe, economical, and satisfactory
manner.
The design and application of coordinative measures by the wire-using companies in-
volve two broad fields of coordination, structural and inductive. Both fields have been
for a number of years and will continue to be under intensive study, directed toward im-
proving methods and securing further economies without sacrificing but, when practicable,
bettering present safety and service.
29. STRUCTURAL COORDINATION
Structural coordination, as the name implies, consists of planning, designing, construct-
ing, and maintaining the physical overhead plant of each company, with due consideration
for the plans and plant of all other companies involved, so that safety and overall economy
will be attained.
SITUATIONS OF PROXIMITY are created when power and communication lines are
so located with respect to each other as to parallel, cross-over, occupy the same poles
(joint use), or require consideration of line wire, guy, or pole-mounted equipment clear-
ances. The overbuilding of one type of service by the other is considered objectionable,
joint use usually being the better solution, with the power wires in the upper position in
all cases of proximity.
The National Electrical Safety Code, Fifth Edition, Part 2 ( National Bureau of Standards
Handbook H32), issued Sept. 23, 1941 (hereinafter referred to as the Code), which has
been approved by the American Standards Association, presents Safety Rules for the
Installation and Maintenance of Electric Supply and Communication Lines. These rules
embody specific minimum requirements, and, though not complete, they are intended to
cover those points which are most important for the safety of employees and the public.
This code is acceptable to the various wire-using organizations throughout the country
and, except as modified by more exacting state or local regulations, is applied, together
with the Principles and Practices discussed previously, generally throughout the country.
Where a certain coordinative problem arises, not specifically covered in the Code, the
companies involved agree on the best engineering solution for the problem. The Code
also provides for modifying or waiving its requirements in any given case where such
requirements are inapplicable, not justified, or impracticable, or where equivalent or safer
construction can be more readily provided by other means. It is, therefore, a practicable
and flexible guide.
Structural requirements and clearances between electric, railway, and communication
structures, wires, and equipment must be adequately provided for, as set forth in the Code.
Owing to the large amount of detailed information necessary in specifying these require-
ments under the numerous conditions encountered in practice, they will not be given here,
but they may readily be obtained from the Code.
Certain fundamental concepts (other than those previously enumerated under Principles
and Practices) in this work are generally accepted as good engineering practice and may
be stated in general terms:
(a) The mechanical design and construction of electric (supply) and comrni.mTCfl.tion
systems should conform to good modern practice.
(b) When changes are made in systems or methods of operation, consideration should
be given to decreasing inductive influences and susceptiveness, when practicable.
(c) Coordinated systems should be maintained, so that abnormal conditions affecting
either service will be minimized and prompt action will be taken to eliminate such condi-
tions when they do occur.
STRUCTURAL COORDINATION
10-69
(tf) Supply, communication, and trolley circuits should occupy levels in the order
named, with supply circuits at the top level. Also, where supply lines carry different
voltages, the higher-voltage lines are usually placed above those of lower voltage.
(e) Joint use should be considered when it can be employed with reasonable safety and
convenience, economically, and without appreciable service detriment.
JOINT USE of poles is a very desirable means of coordinating supply and communi-
cation facilities where this type of construction is feasible. Various types of construction
are employed, depending upon the types of facilities involved, but in any case the con-
struction is designed to conform to the latest practices and safeguards.
,3 3 3
ft
3
3 9
SUPPLY ATTACHMENTS, EXCEPT VER- N
TICAL RUNS, STREET LAMPS, SPAN
WIRES, TROLLEY CONTACT CONDUC-
TORS AND ASSOCIATED FEEDERS, SHALL
PREFERABLY BE ABOVE COMMUNICA-
TION ATTACHMENTS (PART 1- PAR, 2-00
8 8 8J
a a a
_i
COMMUNICATION ATTACHMENTS. EX-
CEPT VERTICAL RUNS, SHALL PREFER-
ABLY BE ABOVE TROLLEY CONTACT
CONDUCTORS AND ASSOCIATED FEED-
ERS ( PARTI -FAR. Z.Ot)
TROLLEY CROSSARMS CARRYING DC
FEEDERS Of NOT OVER 750 VOLTS
NOTE.
REFERENCES, SUCH AS (PART 1-PAFL 2.01) RE-
FER TO THE TEXT IN A REPORT OF THE JOINT
COMMITTEE ON PLANT COORDINATION OF THE
EDISON ELECTRIC INSTITUTE AND THE BELL
TELEPHONE SYSTEM, ENT1TLEO * JOINT POLE
PRACTICES FOR SUPPLY AND COMMUNICATION
ORCmTS," ISSUED OCTOBER 2&,1945
VOLTAGE OF SUPPLY
CIRCUIT CONCERNED
DIMEN-
SION
MINIMUM CROSSARM
SPACIWt IN INCHES
DIMEN-
SION
MINIMUM SEPARATION BETWEEN
CONDUCTORS IN INCHES
0-8,700
A
48
a
•40
OVER -S,700
72
«0
(PART 2- PAR. 1O.O3}
FIG. 1. Relative Position of Attachments, Showing Vertical Clearances and Climbing Space (Joint
Pole Practices for Supply and Communication Circuits, Oct. 29, 1945}
For joint-use construction, commonly employed in urban areas for local distribution,
Figs. 1, 2, 3, and 4 show the usual typical construction features aini clearances eonsidered
good modern practice and meeting Code requirements. Adequate clearances are essential
for the protection of personnel and property.
Normal joint-use construction is applicable to construction involving comrnumoaztion
cables or conductors and supply cables or conductors of the following types:
(a) Constant-potential a-c supply circuits normally operating at voltages between 750
and 5000 volts between conductors and not over 2900 volts to aeutral or ground.
(6) Constant-current supply circuits of not more than 7.5 amp regardless of the voltage,
and of more than 7.5 amp where the open-circuit voltage of the supply transformer is not
more than 2§00 volts.
(c) Constant-potential a-c supply circuits normally operating at more than 5000 volts
between conductors or more than 2900 volts to neutral or ground,, and eonstaiit-ourreat
10-70
TRANSMISSION CIRCUITS
SUPPLY TRANSFORMERS SHALL BE LOCATED /
ABOVE COMMUNICATION ATTACHMENTS EX-^"1 i
CEPT WHERE IMPRACTICABLE BECAUSE Of J
THEIR SIZE OR WEIGHT (PART 1- PAR. 2.02) }
COMMUNICATION CABLE-
SUPPLY GROUNDING CONDUCTORS SHALL BE PROVIDED
WITH AN INSULATING COVERING FROM THEIR LOWEST
POINT UP TO AT LEAST 4O INCHES ABOVE THE HIGHEST
COMMUNICATION OR TROLLEY ATTACHMENT, EXCEPT
THAT THIS COVERJNG NEED NOT EXTEND BELOW THE
TOP OF THE PROTECTION PROVIDED FOR 8 FEET ABOVE —
GROUND AND MAY BE OMITTED, IF THERE ARE NO TROL-
LEY ATTACHMENTS, FROM GROUNDING CONDUCTORS
WHJCH ARE METALLICALLY CONNECTED TO A CONDUCTOR
WHICH FORMS A PART OF AN EFFECTIVE GROUNDING
SYSTEM (PART 2- PAR. 11.04 AND 11,07)
SUPPLY GROUNDING CONDUCTOR
DIMENSION
TRANSFORMER
PRIMARY VOLTAGE
MINIMUM SEPARATION
IN INCHES
A
0-8,700
4-0
OVER Q,70O
60*
(PART 2-PAR. 10.03)
# TRANSFORMER CASES, Oft OTHER APPURTENANCES, IF
EFFECTIVELY GROUNDED* MAY HAVE A SEPARATION NOT
LESS THAN 4O INCHES FROM COMMUNICATION ATTACH-
MENTS
NOTE:
REFERENCES, SUCH AS (PART 2-PAR. 10.03) REFER TO THE
TEXT IN A REPORT OF THE JOINT COMMITTEE ON PLANT
COORDINATION OF THE EDISON ELECTRIC INSTITUTE AND
THE BELL TELEPHONE SYSTEM, ENTITLED "JOINT POLE
PRACTICES FOR SUPPLY AND COMMUNICATION CIRCUITS,"
•SSUED OCTOBER 29,1945
,THIS PROTECTIVE COVERING
MAY BE OMITTED FOR GROUND-
ING CONDUCTORS WHICH:
1. ARE METALLICALLY CONNECT-
ED TO A CONDUCTOR WHJCH
FORMS A PART OF AN EFFEC-
TIVE GROUNDING SYSTEM, OR
2.IN RURAL DISTRICTS, HAVE A
WEATHER-RESISTANT COVgR-
ING (PART 2-PAR. 11.03)
AT LEAST 6 FEET
(PART 2- AR.tl.Q3)
FIG. 2. Supply Transformer Installation, Showing the Separation from Communication Cables and
Conductors (Joint Pole Practices for Supply and Communication Circuits, Oct. 29, 1945)
supply circuits of more than 7.5 amp where the open-circuit voltage of the supply trans-
former is more than 2900 volts, provided that :
1. The supply and communication circuits are so constructed, operated, and maintained
that the supply circuits will be promptly de-energized, both initially and following subse-
quent breaker operations, in the event of contact with the communication plant.
2. The voltage and current impressed on the communication plant, in the event of a
contact with the supply conductors, are not in excess of the safe operating limit of the
communication protective devices.
(d) Any effectively grounded supply cables, located above communication cables or
conductors or carried on effectively grounded suspension strand, where the supply voltage,
between conductors is more than 750 volts.
STRUCTUEAL COORDINATION
10-71
VERTICAL SUPPLY CABLE
OR CONDUCTORS COVERED
OR ENCLOSED
(PART 2-PAR. 11.04)
COMMUNICATION GROUNDING
CONDUCTOR COVERED WITH
WOOD MOLDING
(PART 2- PAR. 11.10)
SUPPLY GROUNDING
CONDUCTOR COVERED
WITH WOOD MOLDING
(PART 2-PAR. JU>7)
APPOXtMATELY 5 INCHES
•VERTICAL COMMUNICATION
CABLE COVERED OR ENCLOSES
(PART 2-PAR. 11.06}
SUPPLY VERTICAL RUN ON ""^V'"
PINS AND INSULATORS ----
(PART 2 -PAR. ti.05 (a)) ~~^^
NOTES: """*
1. DRAWINGS ARE ILLUSTRATIVE ONLY. RE-
QUIRED SEPARATIONS MAY NECESSITATE
LOCATING ATTACHMENTS AT OTHER THAN
THE SAME LEVEL
2. 45" WHERE PRACTICABLE, BUT IN NO CASE
SHALL VERTICAL RUNS HAVE A CLEARANCE
OF LESS THAN 2 INCHES FROM THE NEAR-
EST METAL PART OF THE EQUIPMENT OF
ANOTHER PARTY (PART 2-PAR, 11.02)
PREFERENCES, SUCH AS (PART2-PAR.II.08>
REFER TO THE TEXT IN A REPORT OF THE
JOINT COMMITTEE ON PLANT COORDINA-
TION OF THE EDISON ELECTRIC INSTITUTE
AND THE BELL TELEPHONE SYSTEM, ENTI-
TLED « JOINT POLE PRACTICES FOR SUPPLY
AND COMMUNICATION CIRCUITS." ISSUED
OCTOBER 29, 1945 STREET SIDE
FIG. 3. Location of Vertical Runs (Joint Pole Practices for Supply and Communication Circuits,
Oct. 29, 1945)
The requirements for normal and special joint use conform to Code Grade C and B
construction, respectively, applying mainly to supporting structures, supply conductors,
and clearances.
JOINT-USE &TJRAL LINE CONSTRUCTION at the higher voltages (above 5000
volts) for power and telephone services, though recognized for some time as the best
engineering solution for many situations of power and telephone lines along the same route
and though employed in various specific cases, has presented a number of problems in co-
ordination. In particular, the longer spans and higher voltages for the power circuits and
the increased noise induction from the longer exposures than are normally encountered in
joint-use urban construction are main factors. The rapid growth, within about the last
decade, of rural electrification has greatly emphasized the necessity for a study and solu-
tion of these problems, to permit a more general application of rural j oint-use construction.
For the purposes of study of safe and economical rural joint-use construction at the
higher voltages, several projects of this type were completed and placed in service before
1947 in Alabama, in the light-loading district, and in Minnesota and South Dakota, both
in the heavy-loading district.
The NES Code (Fifth Edition of Part 2) provides that, if the supply circuit will be
promptly de-energized in the event of accidental contact with the telephone plant, and the
resulting voltages on the telephone plant from such a contact will be within the operating
capabilities of the telephone protective equipment, Grade C construction may be employed
in joint use. This provision of the Code has an important bearing on the problems involved
in long-span rural joint use.
For long-span construction, high-strength line wires are necessary; they are generally
of stranded copper or aluminum with one or more strands of steel for power circuits, and
of high-strength solid steel or copper-covered steel for telephone circuits. The minimum.
size of power wire for Grade C construction under the Code is No. 8 AWG medium-hard
drawn copper.
With high-strength line wires for both power and telephone conductors, it was assumed
that their sag characteristics would be sufficiently alike to prevent contacts in the span
under ice or wind loadings or temperature changes, with reasonable minimum separations
10-72
TRANSMISSION CIRCUITS
of the two classes of conductors at the poles. It was also assumed that a very large per-
centage of rural power circuits would consist of one phase wire on a pin at the top of the
pole and a multigrounded neutral below it on a pin or secondary rack, or that the primary
circuit would consist of two or more primary wires on a cross-arm at the top of the pole
and that the multigrounded neutral, if present, would be located on the same cross-arm
or below it.
Where joint rural lines cross fields or other property, which is or is likely to be traversed
by loaded vehicles or farm machinery, adequate wire clearances should be provided.
SUPPLY CROSS ARMS;;'
COMMUNICATION
CABLE
GUYS (NOT PARALLEL TO LINE) SHALL CLEAR SUPPLY
LINE CONDUCTORS ATTACHED TO THE SAME POLE
BY AT LEAST 6 INCHES PLUS QA INCH FOR EACH
fOOO VOLTS IN EXCESS OF 8700 VOLTS
(PART2-PAR.16U33)
__7 STRAIN INSULATORS
'-\RT 2 -PAR. 17.03 (a) (3))
GUYS SHALL CLEAR COMMUNICATION CABLES OR LINE
CONDUCTORS BT AT LEAST 8 INCHES WHERE PRACTI-
CABLE AND W NO CASE LESS THAN 3 INCHES
(PART e-FAR. 16.03)
SUPPLY CROSSARM
V
COMMUNI-
CATION
CROSSARM
THIS INSULATOR MAY BE OMITTED IF THE
POINT OF ATTACHMENT TO THE STUB IS
MORE THAN 8 FEET ABOVE GROUND
(PART 2- PAR. 17.03 OKI)}
TWS INSULATOR MAY BE OMITTED }F SUY IS
NOT CARRIED OVER, OR UNDER OVERHEAD SUPPLY
CONDUCTORS OF MORE THAN 3OO VOLTS TO GROUND
{OTHER THAN THOSE ON THE GUYED POLE)
NOTE' REFERENCES, SUCH AS (PART 2- PAR. 17 03) REFER TO THE
TEXT IN A REPORT OF THE JOFNT COMMITTEE ON PLANT
COORDINATION OF THE EDISON ELECTRIC INSTITUTE AND
THE BELL TELEPHONE SYSTEM, ENTITLED » JOINT POLE
PRACTICES FOR SUPPLY AND COMMUNICATION CIRCUITS,"
ISSUED OCTOBER 2?, 1945
'^^^^
Use of Strain Insulators in Ungrounded Guys (Joint Pole Practices for Supply and Communi-
cation Circuits, Oct. 29, 1945)
Span lengths in the Alabama installations of rural joint use average about 400 ft with
maximum spans of 600 to 800 ft. In Minnesota and South Dakota, the loading conditions
being more severe, the average and maximum span lengths are about 320 ft and 400 ft
respectively.
For noise induction reasons, the separations between the power and telephone circuits
should be kept as uniform as practicable without incurring undue costs or construction
difficulties. (See article 31.)
Electrical protection, to meet requirements, should provide: (a) fuses, circuit-breakers,
or other devices, which will promptly and reliably de-energize the power circuit, if a ground
fault of relatively low impedance occurs; (6) protective gaps, to be connected between the
telephone circuit and the common neutral (or other low-resistance ground) at such intervals
that the impedance to ground of the telephone plant, in case of a power wire contact, will
be low enough, to permit proper operation of the power protective devices.
As experience indicates that the frequency of contacts is very low, the power protective
arrangements are usually more than adequate to meet the above requirements. The tele-
phone circuits in the joint projects, referred to above, employ protectors having a 3-kv
(mis) breakdown to ground, placed at about Va-mile intervals, thus providing a low-im-
pedance path to ground. The current-carrying capacity of the protector must be sufficient
$& meet tike discharge which may result from a contact.
INDUCTIVE COORDINATION 10-73
As a means of limiting induced 60-cycle open-circuit voltages (under normal operation)
on telephone circuits, which are occasionally disconnected from the central office equip-
ment and entrance cables, a drainage device, consisting of a 0.25-juf condenser in series
with a 10,000-ohm resistor from each wire to ground, may be used.
Although experience at present is limited, the feasibility of higher-voltage long-span
joint use in rural areas has been established, and economic studies in progress indicate
that worth-while economies are possible for most new extensions and sometimes even
where power lines have already been built.
HIGHER-VOLTAGE CROSSINGS (involving supply lines of more than 5000 volts
between wires or 2900 volts to neutral or ground) are given special consideration to min-
imize possible contacts between supply and communication circuits. The Code require-
ments for spacings, clearances, and strength of construction are considered to be minimum
and represent the generally accepted practices (except as modified by more exacting state
or local regulations) throughout the United States.
RURAL POWER LINE CARRIER TELEPHONE SYSTEMS, where applicable, are
being placed in operation throughout the country as a means of providing telephone service
to rural subscribers who are accessible from rural power-line systems but not readily so
from rural telephone lines. Although these carrier telephone systems are still in their
early trial periods, it appears that they will eventually be economically useful in furnishing
telephone service to distant farms and ranches which would otherwise require costly
telephone-line construction to reach. Joint practices and agreements covering this type
of operation are in the formative stage.
A more detailed description of this carrier system and its associated installation and
operating features is given in Section 17.
30. INDUCTIVE COORDINATION
Inductive coordination, as it applies to supply (electric) and communication companies,
embraces the principles and practices, agreed upon by these companies, for the design,
location, construction, operation, and maintenance of their respective systems, located in
the same general territory, in such manner as to prevent interference with the furnishing
of either the electric or communication service.
Since much of the general public throughout the country receives both electric and com-
munication service by means of overhead construction, it is inevitable that many situations
of proximity between the two services will be created under a wide variety of construction
and operating conditions. Also, telephone circuits usually transmit relatively low amounts
of electrical speech power (varying from less than 1 to a few milliwatts) , whereas electric
transmission and distribution circuits transmit power ranging from a few to hundreds and
thousands of kilowatts. Owing to the much greater amounts of power carried by these
circuits, not only at the fundamental but also in many cases at harmonic frequencies within
the voice-frequency range, inductive effects from power circuits may, under certain condi-
tions of proximity and operation, severely affect com muni cat ion service, if proper control
is not provided.
The control of inductive interference in communication circuits, to permit giving a
satisfactory service, is accomplished through the application of general coordinated
methods, or, when required, by applying specific coordinated methods, as set forth in the
Principles and Practices, discussed in article 28.
There are two general classifications of inductive interference, namely: (a) noise fre-
quency (induction from power harmonics within the voice-frequency range); (&) low-
frequency (induction from the power fundamental frequency, usually 60 cycles, during
abnormal power circuit conditions).
Inductive effects between power and communication circuits arise from the fact that
power wires, transmitting relatively large a-c voltages and currents, establish strong elec-
tric and magnetic fields in their vicinity, which, owing to their varying character, set up
in nearby communication wires alternately increasing and decreasing electric voltages and
currents of the same frequencies as those in the power wires. Induction from communica-
tion to power wires would have no noticeable effect in any event on power service, because
of the small amount of power carried by the communication wires and the nature of the
power service.
It is often desirable to consider effects of magnetic and electric induction separately,
particularly in the technical analyses of specific problems. This is not only because the
physical processes and the effects of voltage and current induction are quite different but
also because the power-circuit voltages and currents are often affected differently by
10-74
TRANSMISSION CIRCUITS
•esenting
FIG. 5. Diagram Showing Couplings between Power
and Telephone Wires for Electric Induction
changes in conditions. Electric induction is due to the voltages on the power line; mag-
netic induction is due to currents on the power line.
Theoretically, electric and magnetic induction are produced as described briefly below.
A simple method of visualizing electric induction is by means of the capacitances in-
volved with a single power wire and a single telephone wire, as shown in Fig. 5. Neglecting
the impedances outside the exposure (shown dotted in Fig. 5), the voltage of the power
wire to ground (Ep) divides over the capacitances CTP and CTO in proportion to their
impedances (that is, in inverse ratio to
their capacitances) . The induced voltage
(ET) on the telephone wire may therefore
be expressed mathematically as:
^-tsrns;* (1)
Where there are numerous power and
telephone wires, capacitances exist be-
tween every possible combination of wires,
and of wires and ground, resulting in a
complicated network, but the principles
involved are the same as in the simple case
discussed above.
The potential of the telephone wire
to *» the sam/ ^ a!°nS ^length.
the wire is perfectly insulated from
ground, extends only through the length
of the exposure, and has no equipment on it, this potential is independent of the length
of" the exposure (the condition shown in Fig. 5 if the impedances to ground are neglected).
This is true because, whereas all the capacitances in the above equation are proportional
to exposure' length, the ratio CTP/(CTQ + CTP) is independent of length. However, in
practice, the circuits usually extend beyond the exposure and have equipment connected
between them and ground, so that there are impedances to ground outside the exposure
through which longitudinal current will flow. Since the impedance of CTP controls the
total longitudinal current, this current will be practically independent of the telephone-
circuit impedances to ground and will be proportional to exposure length. It will also
be proportional to the frequency of the harmonics in the inducing voltage. Hence, for
given telephone-circuit impedance conditions (outside the exposure), the voltage to ground
will be proportional to exposure length and to the frequency of the inducing voltage in a
uniform and electrically short exposure.
In magnetic induction, the current in the power wire sets up a magnetic field which
alternates at the frequency of the current. If a communication wire is located in this field,
a wltage is induced along it which is pro-
portional to the rate of change of the mag-
netic flux. This phenomenon is illustrated
in Fig. 6. The voltage between the tele-
phone " circuit and ground varies from
point to point along the circuit and de-
pends on the distribution of the imped-
ances to ground as well as on the distribu-
tion of the induced voltage. Also, since
the voltage acts along the circuit and the
part induced in each short length adds
directly to those in all other short lengths,
the total induced voltage is directly pro-
portional to the exposure length in a uniform and electrically short exposure. Further,
as the rate of change of magnetic fiux is proportional to frequency, the induced voltage
will be J>roportional to the frequency of the inducing current.
In the foregoing, the factors discussed apply to both noise and low-frequency induction.
However, these two general types of problems are discussed separately.
Magnetic Flux
FIG. 6. Diagram Showing Coupling between Power
and Telephone Wires for Magnetic Induction
31. NOISE FREQUENCY INDUCTION
Noise frequency induction, in communication circuits, for a given situation of proximity,
depends upon:
(a) Inductive influence of the power circuits, as determined by their electrical char-
acteristics.
NOISE FREQUENCY INDUCTION
10-75
(b) Inductive coupling between the power and communication circuits, as determined
by their physical relation.
(c) Inductive susceptiveness of the communication circuits, as determined by their
electrical characteristics.
INDUCTIVE INFLUENCE. Two characteristics of a power system of primary im-
portance in determining its inductive influence are wave shape and balance.
The wave shape of the voltage or current on a power line is a function of the magnitudes
and frequencies of the harmonics, which may induce voltages of frequencies within the
range ordinarily used in telephone circuits. Induced voltages at such frequencies have
much greater interfering effects than the voltage induced at the fundamental frequency.
The approximate relative interfering effects of telephone line voltages and currents is
shown in Fig. 7 for certain subscriber sets and instruments employed in the Bell System.
o
5
—•—LINE WEIGHTING ADOPTED 1935
WHEN TELEPHONE SETS EMPLOYED
\44 OR 557 RECEIVERS.
1941 LINE WEIGHTING FOR F1A-101
SETS (USING HAI RECEIVERS)
1
\
>7
\
*^.
j 10
P
|25
£30
S3*
40
-45
/
/
\
"**"
\
/
/
^X
^
/
/
\\
/
/
M
/
/
V\
/
1
/
1 ]
15O2OO 4OO 6OO tOOO 2OOO 4OOO
, ' «}EQUENCY W CYCLES PER SECOND
FIG. 7. Line Weightings for Tele-
phone Message Circuit Noise (Rela-
tive Interfering Effects of Telephone
Line Voltages or Currents) (Report
45, J.C.P.C.)
0
5
w K>
§ is
*»
S25
g30
C35
•40
45
— — RECEIVER WEIGHTING ADOPTED
ttJ 1935 (J44 RECEIVER) *
— J941 RECEIVER WElGHTlNC
(HA) RECEIVER)
^*~
/
t-
•^\
/
^
/
Vs
\
t
X
/
s
s
\
N
NV
/
~?^
\
^
\
f
\\
I
t
\
i\i
1
1 1
ISO 2OO 4OO 6OO 100O 2OOO AOOO
FREQUENCY IN CYCLES PER SECOND
*Also applicable to 557 receiver for
estimating receiver noise.
FIG. 8. Receiver Weightings for Tele-
phone Message Circuit Noise (Relative
Interfering Effects of Telephone Line
Voltages or Currents at Receiver) (Re-
ports 32 and 45, J.C.P.C.)
The solid curve shows the line weighting adopted in 1941 for the present-day anti-sidetone
set having a relatively flat response over the useful voice-frequency range. This curve
also takes into account (1) the possible utilization, in future telephone receiving elements,
of a larger part of the wide-band toll transmission attained in the later-type carrier toll
circuits, (2) a more uniform response within the transmission band, and (3) the attenuation
at frequencies near 3000 cycles and higher, relative to that at 1000 cycles, caused by var-
ious types of switching trunks used in toll connections, as compared to the distortionless
trunks used in the tests on which this curve is based. The two curves cannot be compared
on an absolute basis, since the acoustic output per volt input at 1000 cycles is not the same
for the different sets.
Receiver weighting curves for telephone message circuit noise are shown in Fig. 8 for
certain instruments employed in the Bell System. These curves differ from the line weight-
ing curves, principally as a result of taking into account the voltage loss, relative to that
at 1000 cycles, caused by the trunk, loop, and telephone set, between the toll board (at
which point the line weightings apply) and the telephone set receiver.
Each harmonic voltage or current induced in a telephone circuit by a paralleling power
circuit will individually react in the telephone circuit, over which a conversation may be
in progress, and in such a manner that the listener hears the combined effect of all the
harmonics, which is termed noise. Different frequencies in this noise have different
interfering effects, depending on the characteristics of the telephone circuits, type of
receiver, the human ear, and other factors. Relative interfering effects (Fig. 8) are called
noise weightings and have been determined by extensive tests.
Since the effects of electric and magnetic couplings are directly proportional to frequency,
the relative noise influence of power-system voltages and currents is proportional to the
product of noise weighting and frequency. For any frequency, this product times a con-
stant gives the telephone influence factor, TIF. TIF weightings versus frequency are
shown in Fig. 9 for three different periods, reflecting changes in transmission-frequency
characteristics of telephone circuits and instruments from 1918 to 1941. The 1941 curve
10-76
TRANSMISSION CIRCUITS
has not yet been standardized. It will be noted from Fig. 9 that the TIF values at 60
cycles are very low.
While a great deal of inductive coordination work makes use of single harmonic fre-
quency data, there are cases where it is desirable to evaluate the overall influence of a
voltage or current in a power circuit in terms of a single measure. Such a measure may
be obtained by multiplying the magnitude of each harmonic present (amperes for current
14,000
V
1941 (TENTATIVE)
12OO 16OO 2000 2400 2SOO
FREQUENCY IN CYCLES PER SECOND
3200 3600 4000
FIG. 9. TIF Weightings for Periods 1918, 1935, and 1941 (Courtesy A.I.E.E.)
and Mlovolts for voltage) by its TIF weighting, and taking the rss value (square root of
the sum of the squares) of these products. The result for current is the I • T product, and
for voltage it is the KV-T product.
These products can be measured directly with a suitable noise-measuring set and a
current or voltage TIF coupler, the latter having a transmission-frequency characteristic
directly proportional to frequency.
The magnitudes and frequencies of the harmonic currents and voltages on a power line
depend on the characteristics of the apparatus and associated equipment and on the
impedance of the supply line at each of the harmonic frequencies. The wave shape at
various points on the power system depends on the way in which the various harmonic
currents and voltages are propagated over the system. Since power systems are usually
very complex electrically, the propagation effects may vary greatly for different frequencies
and for different systems.
It is impracticable to construct rotating electrical machinery or power transformers
entirely free from harmonics, although marked progress has been made in this respect.
Also, it is inherent in the operation of rectifying devices (and some other types of devices
where the current is not directly proportional to voltage) that harmonics are produced.
Generally speaking, the factors affecting the production of harmonics in these general
classes of apparatus are as follows: ~~"
Motors and Generators. Harmonics are affected by the distribution of air-gap flux,
variations in the air-gap flux due to the slots in the rotors and stators, the distribution
of the windings on the armature, and, in multiphase machines, connections of the windings.
Transformers. The degree of saturation of the iron in the core affects the harmonics
materially. In polyphase transformer banks, the connection of the transformers in the
bank affects some of the harmonics, particularly the triple. In a 3-phase transformer the
arrangement of the core
also affects the triple
harmonics.
Rectifiers. Owing to
the fiat-top wave shape
of rectifier anode cur-
rents, the a-c line cur-
rent, taken by the recti-
fier, has a step-type
wave dbape, as shown in
12- PHASE RECTIFIER
FIG. 10. A-c Line Currents Taken by 6 and 12 Phase Rectifiers
NOISE FREQUENCY INDUCTION
10-77
Fig. 10 for a 6- and 12-phase rectifier. This wave shape results in the production of
harmonic currents and voltages in the a-c line. Table 1 shows the order of these harmonics
(multiples of the fundamental frequency) for various multiphase rectifiers with balanced
operation, and also the reduction, with increase in phases, of the number of harmonics
which are of importance.
The magnitude of any harmonic which is present with any particular number of phases
is the same as for a 6-phase rectifier, assuming all other conditions to be the same. Thus,
the magnitude of the twenty-
Table 1.
third harmonic is the same for
the 6-, 12-, and 24-phase recti-
fiers. Also, the magnitudes of
the harmonic currents bear a
definite relation to the rms value
of the total rectifier current and
decrease in value with increase in
frequency. For a given kilovolt-
ampere input to a rectifier, the
higher the a-c line voltage the
lower is the a-c line current, with
a corresponding reduction in the
magnitudes of the harmonic cur-
rents and usually in the harmonic
voltages resulting from them.
Furthermore, there are generally,
under modern practices, fewer
long closely coupled exposures
with the high-voltage transmis-
sion circuits than with the lower-
voltage power distribution net-
works.
Phase control, employed on
rectifiers for reducing the d-c out-
put voltage below that obtained
without phase control, is accom-
plished by retarding the firing
point of the anodes in the alter-
Harmonics Arising in Rectifiers
Orders of Harmonics in Line with
Balanced Operation
Corresponding
Harmonic
Rectifier Phases
Frequencies
on 60-cyele
6
12
18
24
36
48
System
5
300
7
420
11
11
660
13
13
780
17
17
1020
19
19
H40
23
23
23
1380
25
25
25
1500
29
1740
31
1860
35
35
35
35
2100
37
37
37
37
2220
41
2460
43
2580
47
47
47
47
2820
49
49
49
49
2940
53
53
3180
55
55
3300
59
59
3540
61
61
3660
Note: Higher harmonics are also present for all types listed.
nating-voltage cycle, through grid or firing control. The power factor at the a-c line
terminal of the rectifier transformer is lowered. The magnitude of the harmonic com-
ponents increases in the a-c line current for a given kilowatt output of the rectifier.
Also, with phase control, the anode currents have a steeper wave front at the beginning
and end of the anode firing period, during commutation between successive anodes, result-
ing in harmonics of higher magnitude. Phase control should, therefore, be limited to actual
requirements, particularly at full load and overload ratings of rectifiers, in order to limit
the possible inductive interference.
Balanced and Unbalanced Currents. In a multiphase, balanced power circuit the
voltages between the several phase conductors and between the phase conductors and
ground, and also the several line currents, are vectorially equal to zero.
When the currents or voltages do not vectorially equal zero, they contain a set of single-
phase components, all in the same phase relation, which are termed residual components.
Any system of voltages or currents can be resolved into its balanced and residual com-
ponents, and the effects of each can be analyzed separately. The balanced components are
confined wholly to the phase conductors; the residual components act in a path consisting
of the phase conductors and an external return as, for instance, a metallic neutral or
through the earth. Since the coupling for the residual components is usually much larger
than for the balanced components, the former are usually of greater importance in coordi-
nation problems.
Single-phase branches on three-phase distribution systems are, of themselves, inherently
unbalanced. On grounded neutral systems the residual voltage on a single-phase branch
is practically equal to the phase-to-neutral voltage. On isolated neutral systems the
residual voltage on a single-phase branch depends on the particular system layout. The
single-phase branches also introduce residual currents and voltages on the 3-phase
system.
With the present methods of analyzing noise induction problems, the balanced and
residual currents and voltages are usually considered separately. In the general case of
exposures of overhead lines of the multigrounded neutral type to subscribers' cable cir-
10-78
TRANSMISSION CIRCUITS
Table 2
cults, a knowledge of the residual currents is sufficient, the effect of the balanced currents
being relatively unimportant.
INDUCTIVE COUPLING. The coupling between power and communication circuits
is determined by the degree of their proximity, but it may be greatly modified by the bal-
ance of the two classes of cir-
cuits to each other and by the
proximity of grounded linear
circuits or metallic objects.
In determining coupling, it
is desirable to differentiate
between the effects of the bal-
anced and residual compo-
nents in the power circuit, be-
tween the effects of voltages
and those of currents, and, on
the telephone line, between
induced voltage which acts
directly in the metallic cir-
cuit, termed metallic-circuit
induction, and that which acts
in the circuit composed of the
wires in parallel with ground
return, termed longitudinal-
circuit-induction.
Types of Induction. Eight
components of power induc-
tion, shown in Table 2, need
Types of Induction
Transpositions Tending
to Reduce
Induction (I = Telephone
I
f = rower
A.
Metallic-circuit (direct)
I. From balanced currents
T
2. From balanced voltages
T
3. From residual currents
T
4. From residual voltages
T
B.
Longitudinal-circuit (indirect
metallic-circuit) *
5. From balanced currents
P
6. From balanced voltages
P
7. From residual currents
P
) Only if residuals are
8. From residual voltages
P
) thereby reduced.
* This component of induction can result in noise in the metallic
circuit, because of the reaction of such longitudinal induction upon
self-unbalances (high-resistance joints or leakage) or mutual induct-
ance or capacitance unbalances to other wires on the line or to
ground.
to be considered in noise induction problems. These components vary in their importance,
as noise factors, for different situations and for the reasons discussed above.
Transpositions are employed in open wires within exposures (parallels) between power
and communication circuits as an aid in neutralizing induced power-circuit noise in the
latter circuits. Transpositions are required generally in open- wire communication circuits,
whether or not power-circuit exposures exist, to limit intercircuit cross-talk.
Physical or Side Circuit
X
Types of Phantom Transposftions
Typel
Type 2
Type 3
Telephone Circuit Transpositions
Type 4
Single Pha
Three Phase
Power Circuit Transpositions
FIG. II. Diagrams Showing Wire Arrangements at Transposition Points
NOISE FREQUENCY INDUCTION
10-79
Transpositions are made By interchanging in a uniform manner the positions of the
wires comprising a circuit, so that each wire of the circuit occupies all the pin positions
occupied by the circuit, for distances (usually equal) as determined by the transposition
design. Figure 11 shows the changes employed in the position of the wires (both telephone
and power) at transposition points. Telephone transpositions may be of the physical or
side circuit types involving two wires or of any one of four types of phantom transpositions
involving four wires. Power transpositions may be of the single-phase type involving
two wires or of the 3-phase type, involving three wires.
Identical 3-phase power transpositions, when placed at the l/s and 2/3 points in a given
uniform section of power line, establish a power circuit barrel, since each wire is rotated
120° in phase position and in the same direction of rotation at each transposition. Single-
phase power transpositions rotate the wires ISO0 in phase position. Likewise, for
metallic-circuit induction, telephone transpositions change the phase of the induction by
180°.
Figure 12 shows a simple arrangement of telephone and power transpositions within a
unit exposure length, Z,, containing one power barrel. In this arrangement, which is
Y Y
A A
. L_ , ^ L j^
1. fc
,1
3 *
] 1
3
! ' !
j
"3"
I i
*
! x '
! J i
t
j |
' ! •'
!
i
i Jf
t ! 4
i
i
i I
i i i
j 1
_
i i
f f *
} i
III
i
i
i i
i i
Power
Telephone
a *>•< NEUTRAL POINTS™*- C O
Y » TRANSPOSITION OF ALL PHASE-CONDUCTORS
tl OF A .THREE- PHASE CIRCUIT
FIG. 12. Simple Balanced Arrangement of Telephone and Power Transpositions in a Unit Exposure
Length, L (Courtesy Bell System)
commonly employed, the 3-phase power transpositions are located at neutral points with
respect to the telephone transpositions, and the telephone transpositions are so arranged
as to reduce the direct metallic-circuit induction (from both balanced and residual com-
ponents) within each section of exposure between power transpositions, as well as to limit
inter-cross-induction .
Telephone circuit transpositions tend to
(a) Reduce intercircuit mutual effects, known as cross-induction or cross-talk.
(6) Reduce direct metallic-circuit induction from both balanced and residual com-
ponents of power circuits, within exposures, especially when coordinated.
(c) Balance the two sides of the telephone circuit with respect to earth and with respect
to all other wires on the telephone line, considered as one longitudinal circuit (Sigma) .
These transpositions, by themselves, are not effective in reducing the longitudinal-circuit
induction from either the balanced or residual components of the power-circuit voltages
and currents. However, within an inductive exposure, such transpositions tend in some
measure to equalize these inductive effects by exposing each conductor of the telephone
circuit equally to the power-circuit influences.
For telephone-circuit transpositions to be reasonably effective in reducing metallic-
circuit induction, the relation between the power and telephone circuits within each co-
ordinated section of exposure (with respect to each other, to ground, and to other circuits
present) must be substantially uniform. Thus, points of discontinuity within an exposure,
such as sharp changes in separation, crossings, or changes in power-circuit configuration,
must be considered in inductive coordination work.
Power-circuit transpositions, within the exposure, tend to reduce the longitudinal-
circuit induction from balanced voltages and currents and, as a result, that component of
metallic-circuit noise arising mainly outside the exposure due to the action of the longi-
tudinal-circuit induction (from balanced components) upon any unbalances affecting the
telephone circuits.
Notes. 1. Power transpositions, in the usual case, do not appreciably affect the direct metallic-
circuit induction.
2. That part of the direct metallic-circuit induction which results from residual voltages and currents
is not affected by power-circuit transpositions except in so far as such transpositions may reduce the
power-circuit residuals
10-80
TRANSMISSION CIRCUITS
INDUCTIVE SUSCEPTIVENESS. The degree to which telephone transmission is
adversely affected by noise-frequency induction depends not only upon the magnitudes
of the induced noise voltages, as determined by influence and coupling factors, but also
upon the susceptiveness factors of the telephone system. These include the manner in
which the induced voltages and currents are propagated to the circuit terminals, together
with the reactions of the circuit unbalances (thus relating the current in the terminal
apparatus to the induced voltages), the sensitivity of the receiving apparatus, and the
operating power level of the telephone circuits.
Propagation Effects and Balance. Important differences exist with respect to propaga-
tion effects and balance between open-wire and cable circuits and between toll and ex-
change systems.
As pointed out in the discussion of coupling, only the magnetically induced longitudinal
voltages and currents are important, under the conditions usually encountered, in produc-
ing noise in telephone cable circuits. Because of the negligible effects of electric induction
and direct metallic-circuit induction and because of the important shielding effects exerted
by the cable sheath and the various telephone circuits on each other, telephone cable
circuits are much less susceptive than open-wire circuits.
In open-wire telephone systems, consideration must be given both to electric and mag-
netic induction and to voltages induced directly in the metallic circuit as well as to those
induced in the longitudinal circuit. In a line composed of a number of circuits, the currents
set up in any one circuit depend not only upon the voltage induced in that circuit and its
impedance but also upon the currents and voltages which are set up in the other telephone
circuits on the line. It is not possible, therefore, to calculate precisely the induced currents
merely from a knowledge of the magnitude of the currents and voltages on the power
circuits and the coupling between the power circuits and isolated pairs of wires on the
telephone line, considered independently.
Estimates of receiver noise for a particular type of subscriber set and receiver connected
to a given line circuit, in which noise currents are assumed to be present, may be made as
discussed below.
On the basis of the definition of reference noise, in absolute terms, as an electrical power
of 10~12 watt at a frequency of 1000 cycles dissipated in a receiver (for all types of receivers) ,
Table 3 gives the currents in three types of receivers and the voltages across them at 1000
cycles for reference noise (0 db)
Table 3 and representative values of the
receiver impedances.
At frequencies other than 1000
cycles, the voltage for reference
noise is the voltage across the re-
ceiver producing an interfering
effect equal to that produced by
the reference noise voltage at
1000 cycles. For a given re-
ceiver, the voltage for reference
noise at a frequency other than 1000 cycles may be obtained from the 1000-cycle reference
voltage and the proper noise weighting curve for receiver voltages (if available) . Figure 8
shows such weighting curves for the three receivers listed in Table 3. Also, for a given re-
ceiver, the receiver current for reference noise at a frequency other than 1000 cycles may be
obtained from the relation between the voltage for reference noise across the receiver at the
given frequency and the receiver impedance at the same frequency. Values of receiver
currents and corresponding voltages for reference noise at various odd harmonics of 60
cycles, obtained in accordance with the above procedure, are given in Fig. 13.
From the current for reference noise at a given frequency / and the susceptiveness factor
at the same frequency for a subscriber set, the receiver noise (in decibels) for 1 volt to
ground on the set at that frequency is given by the expression
Receivers
(W.E.
Go. types)
Current,
micro-
amperes
Voltage,
micro-
volts
Impedance,
ohms
144
557
HA1
0.0795
0.1414
0.1210
21.60
19.70
16.56
158 + J221 = 272/54.5°
50 +jl30 = 139/69°
68+jllS = 136/60°
Nf (receiver noise in db) = 20
where I/ — receiver current in microamperes per volt to ground at the subscriber set at
frequency / = suseeptiveness factor for set involved.
IT = receiver current in microamperes (for the type of receiver involved) for refer-
ence noise at frequency / (Fig. 13 for three different receivers).
Values of Nf for the 144 receiver, calculated by the above expression, require no correc-
tions, since present receiver noise transmission impairments are related to noise magnitudes
in this type of receiver. Values of Nf so calculated for the 557 and HA1 types of receivers
are not representative of the interfering effect on the present standard decibel scale of
NOISE FREQUENCY INDUCTION
10-81
noise for the 144 receiver. For the final results of all three receivers to be on approximately
the same basis as to noise transmission impairments, it is necessary to adjust the JV/
values of the 557 and HA1 receivers by factors of -f 4db and — 4db, respectively, which
factors are based on the results of judgment tests. By such adjustments, the readings are
in dba, a term that can be interpreted as representing the quantity that results after
properly "adjusting" the decibel reading of the noise measuring set. When the reading is
thus adjusted all noise results will be on a common basis.
Receiver
>— »
Currents
Voltages
Receiver
Currents j Voltages
144
557
HA1
144
557 |HAJ
144
557 | HAl
144
557
HAl
Fre-
quency,
cpe
Microamperes
Microvolts
Fre-
quency,
cps
Microamperes
Microvolts
180
300
420
4.21
0.954
.586
9.29
2.11
1.27
1.41
0.566
.338
530.
144.
106.
483.
131.5
96.6
60.8
31.7
23.6
1620
1740
1860
0.304
.334
.365
0.505
.549
.586
0.147
.154
.157
112.
128.
146.
101.5
116.9
133.
26.2
28.2
29.9
540
660
780
.40
.281
.180
0.82
.542
.34
.240
.181
.149
80.1
60.6
43.3
73.
55.3
39.5
20.1
18.1
17.1
1980
2100
2220
.373
.376
.377
.604
.598
.593
.158
.156
.154
159.
167.
167.
145.
152.
159.
31.5
32.9
34.4
900
1020
1140
.109
.077
.094
.205
.138
.161
.131
.120
.123
28.7
21.2
27.1
26.2
19.5
24.7
16.7
16.7
18.5
2340
2460
2580
.377
.377
.377
.591
.588
.580
.152
.150
.148
181.
185.
193.
165.
172.
178.
35.8
37.2
38.9
1260
1380
1500
.138
.2
.258
.235
.343
.445
.129
.134
.140
42.4
66.2
91.2
38.6
60.3
83.6
20.5
22.3
24.3
2700
.377
.569
.155
200.
182.
40.8
FIG. 13. Receiver Currents and Voltages Corresponding to Reference Noise.* (Report 46, J.C.P.C.)
* Weighted currents and voltages based on representative receiver impedances and definition of
reference noise as 10~12 watt dissipated in each receiver at 1000 cycles.
Power Level and Sensitivity. The susceptiveness of telephone circuits to induced noise
from power-supply circuits or other outside influences depends to a considerable degree
on the levels of the voltages and currents used in speech transmission and in the efficiency
of the telephone terminal apparatus in converting electrical into sound power. Power
level, as discussed here, refers to the level of speech currents (with respect to reference
level of speech transmission) and not to a level measured in watts.
Speech power, and consequently electrical power generated by a subscriber set telephone
transmitter, which is actuated by speech power, varies over a wide range of values and
frequencies. This variation, will occur with any one speaker and is usually different for
different speakers. Electrical power also varies in different toll and exchange circuits,
owing to the different types of lines and apparatus encountered and line length. In one
investigation, the average acoustic power of speech produced by 16 talkers was of the order
of 10 microwatts. The average ratio of the maximum instantaneous power to the average
power, for the various vowel sounds only, was of the order of 15 to 1, whereas the ratio of
the maximum to average power for a continuous sine wave is 2 to 1, thus showing the
much wider variation of speech power as compared to generated electric power.
The power on commercial telephone circuits is conveniently determined by a device
known as the volume indicator. This device consists primarily of a rectifier-type indicating
meter of specific dynamic characteristics. When measuring speech power, the meter
deflections fluctuate continually in response to the variations of speech power. Because
of this varying deflection, it is necessary to specify a standard method of interpreting the
indications, which involves adjusting a calibrated potentiometer, associated with the
meter, to maintain the meter needle deflections approximately in a specified range on the
scale. When these deflections correspond to the specified reading, with the volume indi-
cator connected across 600 ohms, and the potentiometer is set at zero, the power indicated
by the meter in the circuit being measured is zero YU (volume units).
Since, by the action of the carbon granule transmitter, a relatively large amount of
electrical power is controlled by movement of the diaphragm, the electrical power delivered
to a telephone circuit is much greater (of the order of several hundred tunes) than the
acoustic power delivered to the transmitter. This amplification is of value in maintaining
speech power at satisfactory levels above induced power current levels.
10-82 TRANSMISSION CIRCUITS
Transmitter developments have tended to raise the response level for some frequencies
in order to give a more nearly flat frequency characteristic over the voice range without
materially increasing the maximum level output of the transmitter. Such a characteristic
improves the articulate qualities of the speech and hence effective transmission.
Receiver developments have also increased receiver efficiency over the earlier periods
of operation, in addition to flattening its response over the voice range. However, its
actual efficiency (electrical power input to acoustic power output) is relatively low. The
power loss in the receiver at low frequencies, such as 25 and 60 cycles and their lower
harmonics, is much greater than at frequencies in the higher voice range. The combination
of amplification of voice currents in the telephone transmitter with noise current loss in the
receiver permits delivering to the subscriber satisfactory speech power while keeping
within tolerable limits the sound levels due to ordinary amounts of induced noise.
Speech levels on toll circuits are, in general, maintained at about specified levels by
means of telephone repeaters (not usually employed on exchange circuits) , which amplify
the speech as well as any noise currents and voltages induced in the toll circuits. These
repeaters are usually spaced at suitable intervals on a toll circuit to provide the proper
speech level without overloading the amplifier and without causing cross-induction between
adjacent circuits, due to excessive or inadequate levels.
The trend toward improved balance of party-line subscriber sets and some parts of
central-office circuits permits increasing the speech-to-noise level ratio in exchange plant.
Any betterments of this type, within limits, which increase the signal-to-noise ratio tend
to decrease the noise effects in telephone circuits.
32. NOISE INDUCTION MITIGATION
Noise induction mitigation usually involves careful consideration of at least several
of a large number of factors, which may be broadly classified under the headings: (a) in-
fluence factors; (5) coupling factors; (c) susceptiveness factors.
COOPERATIVE PLANNING in connection with the design and location of lines and
systems is of great importance. These cooperative plans generally are directed toward: (a)
coordinating the locations of lines; (5) incorporating in the design of both systems those
features which will limit the influence and susceptiveness.
By cooperative planning, not only can the number of exposures be limited but also the
general designs of the systems can be made such that treatment of individual exposures
is materially simplified. Furthermore, in connection with new construction or changes
in either system, coordination can be considered before expenditures or other commitments
are made.
CONTROL OF INFLUENCE FACTORS. Residual currents and voltages of the
triple-harmonic series can be controlled by one or more of the following means :
(a) Opening the neutral-to-ground connection of the machine or transformer bant
where the triples originate. This can be done only where other system grounding arrange-
ments, adequate from the standpoint of power system stability and relaying, are available.
(6) Opening the neutral-to-ground connection of transformer banks through which
triples from another source complete their path. System stability and relaying must also
be considered in this connection.
(c) Providing a path for triples (such as with a wye-delta bank), which tends to shunt
them out of the exposure.
(d) The use of wave traps (anti-resonant circuits tuned to the important harmonics),
reactances, or other devices in the neutral-to-ground connections at locations where triples
originate.
(e) The use of transformer connections (such as wye-delta or delta-delta) through
which triples will not pass.
(/) The use of rotating machines, which have a low influence factor.
Note: The last two measures are usually of the greatest importance in connection with cooperative
advance planning, since to change existing equipment to these types may be unduly expensive.
Residual currents and voltages of the non-triple harmonic series can be controlled by:
(a) Reduction of the unbalance which gives rise to them, as by changing single-phase
taps to 3-phase, balancing single-phase taps among the phases of the 3-phase line, or
balancing loads among the 3 phases, where neutrals are multigrounded.
(6) Absorption by wye-delta banks or other means.
In addition to the design of power apparatus to limit, harmonics as far as practicable,
and the. avoidance of excessive magnetic densities, frequency selective devices, to filter
o*xt harmonics, have been used in some situations, for example:
NOISE INDUCTION MITIGATION 10-83
(a) On the d-c sides of trolley rectifiers,
(fc) On the a-c sides of rectifiers.
(c) Across the terminals of rotating machines to reduce important balanced harmonic
currents and voltages.
(d) In the neutral-to-ground connections of generators, synchronous converters, and
other power devices, to reduce triple-harmonic voltages
and currents, an example of which is shown in Fig. 14.
CONTROL OF COUPLING FACTORS. One highly
satisfactory method for the control of inductive cou-
pling, when it can be employed, is the complete physical
separation of the power and telephone lines. However,
in built-up communities both types of service are re-
quired by the public, making it necessary to utilize the
same routes for distribution. For intercity toll lines, ~±r
which are usually important backbone routes for long-
haul communication traffic, frequently reasonable sepa- SUp^ency wMch trap b tUBed to
ration from power transmission systems can be ob- 103
tained, particularly with the proper cooperative advance ~~ ~
planning.
Where power line parallels with open-wire communi-
cation lines (toll or exchange) are created, transpositions
are usually effective in controlling the resulting indue- I?G- 14,- w.ave TraP *& Grounded
tive couplings, and these may be required on a coordi- eu (Repo^S?j!c!p.C Jnerator
nated basis.
Whether the coordination of telephone transpositions with the discontinuities in the
exposure, or the use of power-circuit transpositions, or both, is desirable in a specific case
will depend on the relative importance of direct metallic-circuit induction and longitudinal-
circuit induction acting on telephone-circuit unbalances, and on the importance of the
induction from the balanced and residual components of the power-circuit voltages and
currents.
Telephone transpositions must also be effective in controlling cross-induction (cross-
talk) between telephone circuits. Standard transposition arrangements have been devised
to meet this requirement for different classes of open-wire facilities. Two of such arrange-
ments, which are available, are shown for four arms of wire in Figs. 15 and 16.
Sometimes, unavoidable irregularities occur in the spacing of poles, in distances between
power and telephone circuits, in the presence of shielding objects such as other communi-
cation lines and trolley systems, and in heights of the circuits, which it is not practicable
to take into account in the transposition design. Where these irregularities are large, the
effectiveness of the transposition arrangements is correspondingly impaired.
Possible benefits are illustrated by noise measurements in the rural joint-use exposures,
established in Alabama, Minnesota, and South Dakota (see article 29) . The ratio of re-
ceiver noise to noise-to-ground is a good indicator of the effectiveness of noise-reduction
measures, and such measurements, made under normal conditions, gave ratios of the order
of — 36 db (about 1 to 60 in voltage) , where the IT (effective power harmonic currents in
the line times the voltage interference factor) is fairly high. A ratio of this order is ade-
quate with respect to noise, except in extreme exposures, and should result in noise on
rural joint-use circuits comparable to that on urban party-line circuits in cable.
The favorable noise results in these instances are due partly to the effectiveness of the
transposition scheme used, which employs frequent, point-type transpositions on tandem
brackets and an average wire spacing of only about 7 in. Also in many of the exposures
the power circuit is of the single-phase common-neucral type with vertical configuration,
for which, in joint use, the direct metallic induction into a horizontal telephone circuit is
inherently low. Of course, low values of receiver noise are not obtainable unless the
telephone circuits are well balanced.
Shielding. When either or both of the telephone and power facilities are enclosed in
metallic cable sheath, having a relatively low resistance to ground, the sheath acts as an
effective shield against both electric and magnetic induction. For magnetic induction, the
induced longitudinal currents fiow along the sheath, which has a finite resistance per unit
of length, different from the enclosed conductors, and complete shielding from such cur-
rents is thus not obtainable.
Present trends are toward bonding local distribution aerial cable to multi-grounded
power neutrals, where these neutrals are well bonded to extensive public water systems,
since, in the usual case, the cable sheath becomes quite closely associated with the common
power neutral through the telephone drops, station protector grounds, power secondary
services, and telephone company practices of placing protector blocks between working
10-84
TRANSMISSION CIRCUITS
lines and the cable sheath. Frequent bonds between the common neutral and cable
sheath (about every x/4 mile or less) are not only advantageous from a protection stand-
point but also useful for noise mitigation.
Such bonding usually results in an average reduction of subscriber receiver noise of the
order of 2 to 1 for station sets equipped with single condensers and low-impedance ringers to
ground. The average reduction in noise to ground is about 3 to 1 . In non-public water-pipe
areas the noise reductions obtained by bonding to the neutral depend upon the resistance
to ground of the neutral conductor: the lower the resistance, the greater the reduction.
For power systems of the 2.3/4.0-kv type, increased potentials on the telephone sheath
may generally result from bonding to the power neutral, but tests indicate no cable iusiila-
NOISE INDUCTION MITIGATION
10-85
r 1.2
1st | 3-4
7-8
9-10
Arm }
2nd
Arm
3rd (
Arm"
4th ^
Arm
' .11-12
13-14
17-18
, 19-20
' 21-22
23-24
27-28
. 29-30
' 31-32
33-34
37=38
. 39-40
5-6
15-16
25-26
35-36
45-46
55-56
65-66
75-76
8 16 24 32 40 48 56 64 72 SO 88 96 104 li2 120
NOTE: — The figure at each phantom transposition indicates the type (see Fig. 11).
FIG. 16. Typical Transposition Scheme (Improved Type) for Phantomed Circuits Suitable for Use
in Inductive Exposures (Courtesy Bell System)
tion failures due to this potential increase. In trolley areas, additional direct current will
usually be transferred to the underground
telephone cable sheaths because of power
neutral bonding, but the increase in sheath
current will probably not require additional
corrective measures for electrolysis.
The effectiveness of shielding is expressed
in terms of a shield factor, which is the ratio
of the noise in the shielded to the noise in the
non-shielded condition. Figure 17 shows ob-
served shield factors in four public water
system areas obtained with telephone cable
sheaths bonded to a multigrounded power
circuit neutral at a number of places.
CONTROL OF SUSCEPTIVENESS. In
toll circuits, which are designed to be sym-
metrical with respect to earth, the reduction
of unbalances is usually a matter of correcting
conditions which are the result of deteriora-
tion or maintenance, although situations
occasionally arise where the design of appa-
ratus is involved. The former includes:
(a) High-resistance joints. The remedy is
to make a new joint.
^
**=
==
S52-
*•— «
\
s
\
v
NOISE TO
vGROUNO
t
^
V
I
t
RECEIVER NCHSE,!
PARTY UNE SET >
1-SA RINSE* TO
N
I
(
\
V
\
-v^
\
^
\
SHIELD FACTOR
OL3 CL2 OJ
FIG. 17. Shield Factors — Telephone Cable Sheath
^«^ « ^cw JW1I1U. ... Bonded to Power Circuit Neutral (Courtesy Bell
(o) Leakage caused in open-wire circuits System)
10-86
TRANSMISSION CIRCUITS
by trees or broken or missing insulators. In cable circuits, leakage is usually caused by
moisture entering at a sheath break.
(c) Capacitance unbalances in open- wire circuits. The remedy involves a careful check
of the transpositions either by inspection or by suitable electrical testing means.
(d) Incorrect connections or unbalanced arrangements of apparatus at terminals. For
example, composite sets should not be placed on one side circuit of a phantom group with-
out similar sets being placed on the other.
(e) Incorrect connections in entrance cables, such as split pairs or quads.
In regard to design, the causes of unbalances are usually in terminal apparatus, where
the elements in the two wires of a circuit (or the two sides of a phantom group) are not
sufficiently alike in impedance at noise frequencies. Modern apparatus is usually designed
so that the series impedances and admittances to ground are very closely similar for the
wires in a pair or quad. In some of the older designs, however, the degree of balance
may not be sufficiently high. Sometimes, improvements can be secured by selecting among
existing equipment the units having similar characteristics and grouping them together
on pairs or quads. In some instances, there may be unbalances in entrance cables or
office cabling, for example where phantomed circuits are routed through non-quadded
cables.
In the exchange plant, unbalances due to connections of ringers to ground can be reduced
by the use of high-impedance ringers or by other subset apparatus with improved balance.
Central-office-cireuit unbalances may need to be improved by modifications in or replace-
ments of existing apparatus of the older types and of unsymmetrical design. The more
recently designed central-office equipment is better balanced, and further improvements
in this respect may be expected.
Sometimes improvement can be secured by inserting a balancing impedance in the other
side of the circuit. Through cooperative advance planning, apparatus having improved
balance can be introduced in an orderly manner.
Isolation of equipment unbalances can sometimes be secured by inserting between the
apparatus and the line a well-balanced repeating coil without ground connections or with
ground connections so arranged that longitudinal voltages and currents are not trans-
mitted. It is necessary to arrange the circuit so that signaling and supervision will not
be interfered with. A less effective but sometimes adequate method of isolation consists
of inserting between the apparatus and the line a well-balanced coil so connected as to be
non-inductive to the metallic circuit but to present a high longitudinal impedance. A
well-balanced repeating coil, with the windings suitably connected, will frequently serve
this purpose. This method has the advantage that it can be readily arranged so as not to
interfere with d-c signaling and supervision. In both the toll and exchange plants, it
is frequently necessary to guard against interconnection of balanced and unbalanced
circuits through cord circuits not containing repeating coils, since such a connection would
be unbalanced. This can be done by avoiding the use of such cord circuits for these connec-
tions or by isolating tbe unbalanced lines by repeating coils.
Figure 18 shows a schematic of a typical local step-by-step connector circuit in the
talking condition, with a long
UOK6 UKE cmcurr LOCAL coKNECTQ* Hne ^^ inserted adjacent
R to the line in order to prevent
longitudinal current flow from
the calling line causing noise,
due to possible unbalances in
relays A and D and in the 2-
yuf series condensers. This is
one means of preventing lon-
circuit noise reach-
called subscriber from
a connected line which is
affected by power induction.
Transmission Levels. The effect of noise is lowered as the power level of the voice
currents of telephone circuits is raised. In the toll plant, this fact has had a marked
bearing on the sizes of wire used and the location of repeater stations. One of the limita-
tions on the degree to which levels can be raised on toll circuits by repeaters is the difficulty
of avoiding cross-talk between circuits on which there are large level differences. Subject
to this limitation, however, advantage may sometimes be taken in specific situations of
allocating repeater gains in such a way as to use the highest practicable level through
inductive exposures.
In the exchange plant, telephone repeaters are normally not employed, so that the con-
trol of levels in connection with specific noise situations is a less practicable procedure.
ZMF
FIG. 18. Schematic of Typical Local Step-by-atep Connector Cir-
euit in Talking Condition Associated with a Long Line Circuit
(Courtesy Bell System)
NOISE INDUCTION MITIGATION
10-87
However, the desirability of utilizing the highest practicable. levels has had an important
bearing in the development of instruments, cables, and other facilities.
Other Devices. In special cases, neutralizing transformers, resonant shunts, or resonant
drainage to ground, applied to the telephone circuits, offer possibilities as coordinative
measures for the reduction of noise induction.
The neutralizing transformer is employed, primarily, in local communication circuits
serving power stations to limit voltages to ground at such stations when power-line faults
ACCIDENTAL
GROUND
-NOTE — X
IN A PRACTICAL SITUATION X.
THE EQUIPOTENTIAL LINES
WOULD NOT BE AS REGULAR
AS INDICATED
* FIGURES USED AS
ILLUSTRATION ONLY
FIG. 19.
Diagram Illustrating Rise in Station Ground Potential Due to Power Line Fault (Report 44,
J.C.P.C.)
occur. Without the transformer, the rise in potential of the power station ground, and
consequently the telephone set protector ground, would frequently be enough to break
down the protector blocks and disable telephone service, as shown in Fig. 19. With the
transformer, differences of potential between the communication circuit and nearby
grounded structures are materially reduced, as indicated in Fig. 20, thus minimizing
hazard to personnel, cable troubles, and service interruptions.
PROTECTOR r V-> "* PROTECTOR
BLOCKS ^
-^TOT^
BLOCKS
f 6X^
1 f
I
TO \ (3)
SUBSCRIBER KVo—w
SHIPMENT / R
C±D
^
^b
| ^~[
•j
R\
TO
CENTRAL
OFFICE
EQUIPMENT
/
^
1 f<~\ r^,,
v?
-nwr*-
T
\
\
Tf
* o VJD.
Vp
rCJL/4 •" v.yy '"Yn^"vvv
"S PQWER-
— L_ STATION
— GROUND
""f CENTR
— I— OFFIC
CENTRAL-
OFFICE
~ GROUND
^ GROUND ~
(T) CONNECTION MADE VIA CABLE SHEATH WHEN AVAILABLE.
(?) USE REMOTE GROUND WHEN NO CABLE SHEATH IS AVAILABLE.
(3) REMANENT VOLTAGE (VR) = V,-V2. "K* WILL HAVE A VALUE
BETWEEN 1/2 AND t DEPENDING UPON CIRCUIT CONDITIONS.
FIG. 20. Diagram Illustrating Action of Neutralizing Transformer in Neutralizing Voltages on a
Circuit Subject to Ground Potential Rise (Report 44, J.C.P.C.)
Ground Return Circuits. Ground return telephone circuits, being inherently unbalanced
to ground, require methods of coordination with power circuits different from those em-
ployed for metallic telephone circuits, such as previously discussed in this section. Ground
return power circuits are not considered standard practice but are frequently operated
as single-phase grounded neutral circuits in rural power systems. Coordinative measures
are available for this type of power circuit with metallic telephone circuits, such as control
of power-circuit influence factors and transpositions, drainage coils, or high impedances
(to predominating harmonics) inserted in the telephone circuit.
10-88
TRANSMISSION CIRCUITS
33. LOW-FREQUENCY INDUCTION
Low-frequency induction, under normal balanced power system operation, rarely creates
a noise problem in communication systems. However, under some normal operating
conditions, the induced ground- wire (for lightning protection) current flow at the power-
circuit fundamental frequency may be objectionable, particularly in telegraph operation.
When an abnormal condition, such as a grounded phase wire, occurs on a power circuit,
relatively large currents at the fundamental frequency flow from the power circuit to
ground for grounded power systems. This may result in excessive low-frequency induction
in any paralleling communication circuits. This condition also obtains in an isolated power
system when two or more phases are faulted.
The magnitude of the voltage induced in a telephone circuit at the time of a power-
circuit fault depends chiefly on the magnitude of residual currents and on the exposure
conditions.
Residual Currents. If 1 phase of a 3-phase power line develops a fault to ground the
currents in the 3 phases become unequal, and their vector sum, which is the residual
current, is no longer zero. In most low-frequency induction problems, residual current
is far more important than residual voltage.
The relatively large inductive influence of residual current is due to the fact that it
exists in a circuit consisting of the line conductors in parallel as one side and the earth
as the other side. Since much of the return current is deep in the earth, its neutralizing
action is small.
The chief factors that determine the magnitude of the residual currents are (1) the power-
circuit voltage, (2) the line and apparatus impedances, (3) the fault and earth impedances,
(4) the impedances of the neutral ground connections, (5) the type of ground wire, if used,
and (6) the circuit configuration including ground wires.
In analyzing the impedances controlling fault current, two general types of power
systems must be considered: the grounded neutral, and isolated neutral systems. These
are illustrated in Fig. 21. In the
Transmission Line Transformer_ grounded neutral system, the neutrals
of one or more transformer banks are
grounded directly or through imped-
ance so that, in the event of a fault, a
path for current is established from
the fault through the earth and return-
ing through the neutral-to-ground con-
nections. In the isolated neutral sys-
tem, there are normally no grounds on
the system so that, in the event of a
fault, the path for fault currents is
through the capacitances of the un-
faulted phases to earth. Hence, for a
single fault, the fault current is limited
to the charging and leakage current.
If, in an isolated neutral system, a
second fault to ground occurs on
another phase while the first persists, a
residual current will flow between the faults. Simultaneous faults on two phases at
different points may occur on any type of system but are more likely to occur on an
isolated neutral system than on one in which the neutral is solidly grounded. This is
because, for the isolated system, full phase-to-phase or possibly higher voltage is impressed
between the unfaulted phases and ground, thus increasing the voltage stress on the insu-
lation of the entire system during the time of fault.
A system grounded through a neutral impedance has some of the characteristics of an
isolated neutral system. Generally, the addition of neutral impedance tends to reduce
the fault current, this effect being proportionately larger for faults near the neutral ground-
ing points. This reduces the voltage induced on nearby telephone lines and may have
advantages to the power system. On the other hand, increasing the neutral impedance
may introduce problems in power system relaying. It may also increase overvoltages on
the power system.
The duration of residual current is also important, since the length of time that the
induced voltage persists has important reactions on its effects. For example, with the
carbon block protectors, the chance of their becoming permanently grounded, with con-
se<nient interruption of service, depends not only upon the amount of current through
(a) Isolated System with Delta Connections
Supply
Transformer
Transmission Line
Load
Transformer
(6) Grounded System with Delta-wye Connections
FIG. 21. Power System Arrangements with Isolated and
Grounded Connections
LOW-FREQUENCY INDUCTION
10-89
the protector but also upon its duration. Likewise, other effects which are described later
are materially affected by tl^e duration of the induced voltage. Since, except for self-
clearing faults, the duration of fault current is determined by the time of operation
of the power-current interrupting devices, their reliability and speed of operation are
important.
COUPLING FACTORS. Coupling is proportional to the length of the exposure for
uniform separation. It varies with separation in a manner which is affected, among other
things, by the structure of the earth. This effect can be summarized as follows:
Under the conditions of low-frequency induction, the telephone wires comprise one side
of a loop, the other side of which is the earth. Likewise, the power wires comprise one side
of a loop, the other side being the earth. The magnetic coupling between two parallel
loops at a given separation increases as the size of the loops increases. The sizes of the
loops are determined by the distribution of the return current in the earth. Generally
speaking, the greater the resistivity of the earth, the more the current will spread and the
greater will be the coupling to an adjacent circuit.
The effect of earth resistivity on coupling is much greater for wide separations than
where the lines are close together. Consequently, with high-resistivity earth, not only is
the coupling higher at all separations than with low-resistivity earth, but (except for very
wide separations) the percentage reduction secured by increasing the separation a given
amount is smaller.
Figure 22 shows, for several earth resistivities, the variation of mutual resistance,
reactance, and impedance with separation, based on calculations using Carson's formula
and a frequency of &0 cycles, without shielding.
gO.OOO*
s
NOTE: SHIELDING EFFECTS NOT A FACTOR
IN COMPUTING ABOVE CURVES.
MUTUAL IMPEDANCE
-——>—--— MUTUAL RESISTANCE
MUTUAL REACTANCE
HEIGHT OF POWER LfNE, hi = 50 FT
HEIGHT OF TELEPHONE; LINE, H2 =25 FT
EARTH RESISTIVITY p, IN METER^OHMS
10
40 60
KX> 20O 4OO 6OO IgOOO 2XKX5 4«OOQ 10<000 20.000
HORIZONTAL SEPARATION IN FEET
FIG- 22. Variation of Mutual Resistance, Reactance, and Impedance with Separation (at 60 cycles)
(Report 14, J.C.P.C.)
SHORT-CDR.CTJIT CURRENTS, during power-line faults, may be calculated by several
approximate short-cut methods, one of which may briefly be described as follows:
(a) Prepare a diagram of the power-system network, showing lengths, location, and
kva capacities of large generating sources and transformer banks; location, kva capacities,
and connections of grounded neutral transformer banks; and magnitudes of neutral im-
pedances, if any.
(b) Show the location and separation of the telephone-circuit exposure or exposures to
the power-system network.
(c) Show the ]ine-to-line operating power voltage.
10-90
TRANSMISSION CIECUITS
too
so
§40
GENER-J STEAM TURBO l_ _
ATORS \HYDRO DRIVEN 35% A
SYNCHRONOUS
CONDENSERS 35%
OjOI CLO2 O^4 O.J
(UNE-KV>2
CONNeCTED TRANSFORMER KVA
0,4 0.6 tO 2. 468 10 20 406000
CONNECTED TRANSFORMS]
GROUNDED '
3 TRANSFORMER KVA
TRANSFORMER KVA
too
80
RANGE TYPE OF
IN KV GROUND WIRE
t tt-33 1
2 44-66 I NONE OR LOW
3 75- HO f CONDUCTIVITY .
4 I32-220J
* ^A-Wk
5 44-220
HKSHCON-
-
\\
2 4 e a 10 20
^ACTUALLY. IMPEDANCE BUT USED
AS REACTANCE
\
\
\
\
J\
\N
N>VN
\
W)
\
40 6O 1OO 20O 4OO £00
CALLOW FOR NEUTRAL AND FAULT IMPEDANCE
AS INDICATED JN TEXT
FIG. 23. Curves for a Quick Approximation of Fault Current Resulting from Single-phase Faults
to Ground on Three-phase Systems (Courtesy Bell System)
(<3) Using the various curves a, b, c, and d in Fig. 23, determine for a given situation :
i -c- f (line kv)2 _
1. Xj. from ; — ; using Fig. 23a.
(connected transformer kva at source supplying fault)
0 _ _ connected transformer kva _.
2. F - XA. from 7—7— — , usuig Fig. 236.
grounded transformer kva
Note: Connected transformer kva and grounded transformer kva refer respectively to (1) total con-
nected capacity, irrespective of transformer connections, and (2) transformer banks, which will
pass zero sequence current.
3- XL — apparent reactance (actually impedance) of equivalent power line mileage
from source to fault. (Use actual mileage, if only one power circuit is involved), using
Fig. 23c.
4. X = F - XA + XL.
5. Z — V.R2 -f X2, where R = neutral and fault resistances, if any.
6. Short-circuit (fault) current //, using Fig. 23<2.
*
Notes: If connected generator kva is more or less than the connected transformer kva by a factor of
2 or more, use connected generator kva supplying fault, for Figs. 23a and b.
If a reactance JTjv is used in the grounding neutral, replace X with X + X&.
Figures 23a, c, and d are based on the following assumptions:
1. A single 60-cycle generating station.
2. Radial transmission line.
3. Total connected transformer kva at station equals connected generator kva.
4. Line side neutrals of all transformer banks are grounded and will pass zero sequence current.
5. All transformer and generator capacities are so bussed as to be effective in supplying faulted line.
6. All transformers have S per cent reactance, based on kva rating of bank.
7. Representative average conductor spacings and sizes.
8. Earth resistivity of 100 meter-ohms (in the case of Fig. 23c).
The above ^procedure is not to be considered an exact method of short-circuit current
calculation, since it usually provides only a rough determination, the method of symmet-
rical components being the proper one for more accurate results (see Electrical Engineers
Handbook, Vol. 1, Electric Power, H. Fender and Wm. A. Del Mar, John Wiley & Sons).
LOW-FREQUENCY INDUCTION
10-91
Having determined the mutual impedance ZM-, and short-circuit current I/, for any
given situation and power line fault, the longitudinal induced voltage J?/, on the adjacent
communication aerial open wires or cable, is given by the expression
Ef = If • ZM- TJ
(Ztf from Fig. 22 or similar curves; 77 = shield factor.)
SHIELDING. Another important factor in determining the net coupling is the effect of
grounded wires or other linear grounded metallic structures along the exposure. Voltages
are induced in such grounded metallic structures in the same way as they are induced in
telephone wires, and these voltages establish currents. The induced currents flowing in
MESSENGER SIZE
25 M 1/2* DIA. WM 7/16* DlA. JOM 3/8* DIA,
-f-=END GROUND RESISTANCES PER
* UNIT OF CABLE LENGTH ; OHMS/KF
0>
&
X
X
X
X
X
TO GROUND
TO SHEATH
O.O6
003 Of O.15 O2 O.3 0.4 O.5 O.8 O.S LO J.5
D-C RESISTANCE OF SHEATH IN OHMS PER KJLOFOOT
*SHICLD BACTORS ARE FOR VOLTAGES APPEARING AT ENDS OF
AN AEtfUfc CABLE WHICH IS GROUNDED ONLY AT THE ENDS,
FIG. 24. Shield Factors for Asrial Lead Cable at 60 Cycles (Report 48, J.C.P.C.)
these structures set up magnetic fields, which generally oppose those from the power wires
and reduce the induction in the telephone circuit. The effect of such currents in grounded
structures is known as shielding.
The magnitude and phase relation of the current in a grounded conductor, and thus the
shielding provided by it, depend on the impedance of the conductor with earth return.
Hence, the shielding is increased, when the resistance of the conductor and its ground
connections is reduced. Metallic cable sheaths comprise an important type of shielding
conductor, as shown in Fig. 24 for aerial cables with plain lead sheath at 60 cycles; R is
the sum of ground connection resistances at both ends of the cable sheath (in ohms) and
S is the length of cable circuit between terminals or grounds (in kilofeet). With increasing
end-ground resistance, the shield factors for voltages measured to ground increase, while
the shield factors for the voltages to sheath (between sheath and conductors) decrease.
The earth resistivity was assumed to be 100 meter-ohms. Figure 25 shows shielding
effects at 60 cycles from grounded telephone open wires.
In analyzing the distribution of induced voltage between a telephone circuit and ground,
assume first that no protectors are operated. Under this condition, the voltages to ground
10-92
TRANSMISSION CIRCUITS
FREQUENCY* eO CYCLES
EARTH RESISTIVITY =
tOO METER -OHMS
R=SUM OF RESISTANCES OF END
GROUND CONNECTIONS IK OHMS
U= DISTANCE BETWEEN END GROUND
CONNECTIONS IN KJLOFEET
on the telephone wires at various points are determined by the impedances between the
wires and ground along the line and at central offices where equipment is connected to
them. The^voltage to ground at either end of the exposure is equal to the product of the
longitudinal -current and the impedance to ground seen looking away from the exposure
at that end. In practice, the
variety of impedance distri-
butions encountered is almost
infinite, and the correspond-
ing voltage distributions vary
over a wide range.
If voltage to ground at any
point where protectors are lo-
cated exceeds the operating
voltage of the protector, the
protector operates and three
things happen:
(a) The voltage to ground
at the point of protector
breakdown is reduced to a low
value. This causes an in-
crease in voltage across the
protectors at the opposite
end, and in most cases they
also will operate.
(6) The operation of the
protectors at the two ends
completes a loop consisting of
the telephone circuit and
„,.,,. « , . , ,-1 •,- f ^ •, j. ground, so that the induced
Shielding Resulting from the Grounding of Conductors -,, -n j_ ^
voltage will cause current to
16 20 24 28 32 36
NUMBER OF GROUNDED WIRES
of an Open-Tnre Telephone Line (Courtesy Bell System)
flow through both protectors.
(c) The voltages to ground on the circuits on which protectors have operated are
changed and redistributed, and the voltages on the other telephone circuits are also
changed and redistributed, owing to shielding.
All these effects take place within a very short time after the induced voltage is applied,
so that, for all practical purposes, they can usually be considered instantaneous.
ACOUSTIC DISTURBANCE. Strictly the term "acoustic disturbance" should be
used only with reference to the effect of an abnormally loud sound on a person subjected
to it. The term has also come to designate a noise (usually transient) in a telephone
receiver, the intensity of which is considerably higher than that of speech. It is produced
by an excessive voltage across the terminals of the receiver.
Although induced voltages usually appear in equal magnitudes on the two sides of a
circuit, the protector gaps on the two sides of the circuit discharge in an unsymmetrical
manner, with the result that a voltage higher than normal appears across the circuit.
When this occurs, a loud noise is pro-
duced in the receiver of a telephone
set bridged across the circuit, causing
acoustic disturbance. This may be
produced by low-frequency induction,
lightning, contacts between power
and telephone circuits, and by other
causes.
Figure 26 shows oscillograph traces
of voltages measured across operating
protector blocks. Each outside trace
(a)
Na.3j
3 Element
Oscillograph
FIG. 26. Oscillograms Showing Protector Performance
with Impressed Potentials across the Protector Blocks
shows the voltage across its related
block to ground. It will be noted that
the two traces are not identical. The
middle trace shows the resulting voltage across the circuit. It is this voltage that may
cause acoustic disturbance. The very jagged outline of these traces indicates that many
frequencies are present.
PROBABILITY FACTORS. In the preceding discussion, a number of factors were
mentioned which may vary between different occurrences in the same exposure. Among
them axe i
(a) The impedance in the faulted circuit. This varies with the location of faults,
LOW-FKEQUENCT INDUCTION 10-93
effective fault resistance, and other factors, with consequent effect on the magnitude of
the fault current.
(6) The duration of the fault current. This varies with conditions that affect the speed
of operation of the power-circuit interrupting devices.
(c) Longitudinal voltage, voltage to ground, and current through protectors. These
may vary widely with small variations in the locations of faults when they occur within
the exposure.
(d) Shielding due to the operation of protectors on telephone circuits. The number of
protectors that operate may vary widely, depending on their characteristics and the mag-
nitude of the induced voltage.
LOW-FREQUENCY INDUCTION CONTROL, though not usually required under
normal operating conditions, must be planned for in advance where service may be affected
by abnormal power-circuit conditions and where prompt action must be taken to restore
normal operating conditions when abnormal conditions arise. Cooperative advance
notices of construction and eoordinative plans are essential in controiling the generally
serious effects of low-frequency induction.
The low-frequency coordination of power and communication systems may be accom-
plished by (1) measures in the power system to limit the influence, (2) measures in the
communication system to limit the susceptiveness, and (3) coordinated location of lines
or other means to reduce coupling. In a specific situation, one measure may be sufBcient
or two or more measures- may be required, depending on the conditions.
POWER SYSTEMS. Measures to reduce the inductive infiuence of power systems
should be directed to limiting the magnitude of unbalanced currents and voltages, par-
ticularly under abnormal conditions, and to reducing the duration and frequency of occur-
rence of faults. Of such measures, some are concerned with questions of Kne and system
design and must be incorporated in the construction plans and others may be added later,
if found necessary as the result of operating experience.
Fault-resistive Design and Construction. Since lightning is a major cause of faults
on power systems, the developments in methods of lightning protection have substantially
aided the low-frequency coordination problem.
Fault-current Lmitation. Resistors or reactors in the neutrals^ of power systems provide
a means of limiting the magnitude of the residual currents except when double faults occur.
Shielding. Ground wires on a power line, though they may increase the total residual
current, provide shielding by reducing the strength of the external electric and magnetic
fields. Under fault conditions, ground wires generally reduce the voltages induced in
paralleling communication circuits. The effectiveness of such shielding depends on the
impedance of the shielding conduetor and its ground connections. Under favorable condi-
tions, the induced voltage at 60 cycles may be reduced about 40 per cent by the use of
one wire, and about 60 per cent by the use of two wires. However, such shield wires may
increase the normal 60-cycle induced voltage, and this reaction may be important where
ground-return telegraph circuits are involved.
High-speed Circuit Breakers and Relays. High-speed relay and switching systems
have been developed that reduce the tune duration of a power-line fault to the order of
Vs second or less under favorable conditions, thus tencling to minimize the effects of
induction. Because of the expense, high-speed switching can seldom be justified except
on important high-voltage transmission systems.
Improvement in Balance. Low-frequency induction between power and communica-
tion lines is sometimes- experienced under normal operating conditions. On grounded
telegraph and" signal lines, the trouble usually manifests itself by a chattering of telegraph
instruments or by false signals. Sometimes power-line transpositions will aid in these
situations.
COMMUNICATION SYSTEMS. la general, coordinative measures, applicable to the
communication system, take the f orna of arrangements or devices for removing or counter-
acting the voltages, the voltage to ground, or the current through telephone protectors.
Relay Protectors. The short-circuiting relay (SCR) protector is designed for applica-
tion to open- wire telephone Hnes which may be subjected to low-frequency induction of
sufficient magnitude to warrant the costs of providing it. This device employs, for each
open-wire circuit, a relay which short-circuits the usual protector blocks associated with
the circuit and grounds the circuit. In one device of this type (Fig. 27), a master relay
controls operation of all of the individual circuit relay st the master relay operating in about
0.01 second and the individual relays about 0.15 second later, after any one of the line
protector blocks operates. The master relay operates when about 1 amp or more of 60-
cycle current flows through the primary winding of the saturating transformer to ground.
This produces a voltage across the secondary of the transformer, operating the master
"J" type relay, causing the short-circuiting relays to operate and short-circuit each line
10-94
TRANSMISSION CIRCUITS
and its associated protector blocks. The master relay can be adjusted to release on about
0.8 amp of line current. Thus, with operation of the pilot relay, all relays operate on
about 0.5 amp direct current and ground all wires on the line at the locations where this
equipment is installed. The equipment may be installed at any outside point on the open-
wire line or in the central office, as desired. It is assembled in groups for application to
10 to 50 or more wires and, together with the dry-cell batteries for operating the circuit
relays, is housed in standard cable terminal boxes.
Acoustic Disturbance Reducers. One of the most effective ways of reducing acoustic
disturbance to operators is to shunt their receivers with a device that will have a high
impedance at speech level and a low impedance at acoustic-disturbance level. One such
device that has proved effective consists of oppositely poled copper oxide rectifier disks
connected across the receiver. These have the property of greatly diminishing impedance
with increasing voltage.
Shielding. Shielding on a telephone line may be effected by special grounded conduc-
tors, by working conductors, or by cable sheaths. Miscellaneous structures, such as pipe
TO LINE J
TOUNE
PROTECTOR
PROTECTOR
ATIN6
B
LOCKS
B
LOCK
5
31 L
RATING
FORMER)
^C
hrOI}-
-00
f
][}-
TO ALL UNITS
IN PROTECTOR
jr £ !
1 ...
SHORT
d*~
X
o 11
P
Q*
' RELAYS v
no
Pll
L
-Jn
1
1
'g'J-TYPE
r
Jo RELAY
TO REMAINING
>~^
3 RELAYS tN
:o
GROUP 1
NO
TO
INTERMEDIATE
5
L
GROUPS
T
TO LAST CROUP
FIG. 27. A-c Type Short-circuiting Relay Protector Circuit — Multi-grounding (Report 41, J.C.P.C.)
lines or rails in the immediate vicinity of an exposure, also introduce shielding. A high-
conductivity shield wire, well grounded at the ends of the exposure and at intermediate
points, may reduce the induced voltage by as much as 40 per cent at 60 cycles.
The lead sheath of a 2 5/g-m.-diameter aerial telephone cable, if effectively grounded
at the ends, reduces the voltage induced in the conductors within the cable by about 50
per cent at 6X3 cycles. Ihe shielding secured from the sheath of an underground cable of
this size is also about 50 per cent. The large number of conductors in a cable affords mutual
shielding which varies from a negligible to a considerable amount (sometimes exceeding
95 per cent), depending upon many factors, important among which is the extent of the
cable beyond the ends of the exposure and the grounding conditions on the circuits at their
terminals. If two or more cables are close together through an exposure, each benefits by
the shielding action of the others, so that the shielding increases with the number of cables.
If the lead sheath of the cable is surrounded by magnetic material, as by armoring or
placing cable in iron pipe, the shielding may be largely increased. With a form of iron
tape armored cable, shielding at 60 cycles may be SO per cent or more, assuming effective
grounding.
Other Measures. Sometimes drainage and neutralizing transformers may be of use.
Drainage is achieved by grounding the midpoint of a coil connected between the two sides
of the communication circuit, the coil being wound in such a way that it presents a low
impedance to longitudinal currents and a high impedance to alternating currents in the
metallic circuit. The voltage to ground on the communication circuit at the point where
the drainage is connected is limited to the voltage drop over the impedance of the coil
and ground connection.
The neutralizing transformer introduces into the exposed communication wires a voltage
in opposition to the disturbing voltage, thereby partly neutralizing it, as described under
"Noise Induction Mitigation'* in article 32.
On account of the cost and the operating limitations that these measures impose on
the use of carrier, d-c telegraph, and testing, they have only occasionally been employed
in the commercial telephone plant. Neutralizing transformers have, however, been used
on telegraph circuits and for special protection purposes on other types of communication
and signal circuits.
BIBLIOGRAPHY 10-95
BIBLIOGRAPHY
Principles and Practices
1. Reports of Joint General Committee of Edison Electric Institute and Bell Telephone System:
(a) Principles and Practices for the Inductive Coordination of Communication Systems, Dec. 9, 1922.
(6) Principles and Practices for the Joint Use of Wood Poles by Supply and Communication Com-
panies, Feb. 15, 1926.
(c) Inductive Coordination — Allocation of Costs between Supply and Communication Companies,
Oct. 15, 1926.
2. Reports of Joint General Committee of American Railway Association (now Association of Amer-
ican Railroads) and Bell Telephone System:
Inductive Coordination of Railway Electrical Supply Facilities and the Communication Facilities of
the Bell System, Apr. 15, 1931, and Sept. 1, 1932.
3. Reports of Joint General Committee of the Edison Electric Institute and the Western Union Tele-
graph Company:
Physical and Inductive Coordination of Electrical Supply and Communication Systems, July 22, 1935.
4. Reports of the Joint General Committee of the Edison Electric Institute and Bell Telephone System
entitled Physical Relations between Electrical Supply and Communication Systems (EJ3.I. Pub.
M5).
5. Year Book of the American Standards Association (ASA).
6. Report of the Joint General Committee on Plant Coordination of the Edison Electric Institute
and Bell Telephone System entitled Joint Pole Practices for Supply and Communication Circuit*
(E.E.I. Pub. M12), Oct. 29, 1945.
7. Safety Rules for the Installation and Maintenance of Electric Supply and Communication Lines
(National Bureau of Standards Handbook E32, Sept. 23, 1941) (N.E.S. Code — 5th Edition).
8. Discussion of the National Electrical Safety Code, Fifth Edition, Part 2, and Grounding Rules
(National Bureau of Standards Handbook H39), July 15, 1944.
9. Specification 1-B-l for Communication Lines Crossing the Tracks of Railroads, Association of Amer-
ican Railroads.
Tecnnical Data
1. Bibliography on Inductive Coordination by American Committee on Inductive Coordination (1925).
(List of articles and reports published before Jan. 1, 1925.)
2. Symposium on Coordination of Power and Telephone Slant, AJ.E.E. Trans., Vol. 50, 437-478.
Part I: Trends in Telephone and Power Practice as Affecting Coordination, by W. H. Harrison
and A. E. Silver. Part II: Status of Joint Development and Research on Noise Frequency In-
duction, by H. L. Wills and 0. B. BlackwelL Part III: Status of Joint Development and Research
on Low-frequency Induction, by R. N. Con well and H. S. Warren. Part IV: Status of Coopera-
tive Work on Joint Use of Poles, by J. C. Martin and H. L. Huber. (These papers include
references to the more important papers published before January 1931.)
3. Experimental Studies of Arcing Faults on a 75-kv Transmission Line, AJ.E.E. Trans., VoL 50,
1469.
4. Effects of Rectifiers on System Wave Shape, AJ.E.E. Trans., Vol. 53, 54*
5. Petersen Coil Tests on 140-kv. System, AJ.E.E. Trans., Vol. 53, 63.
6. Iron Shielding for Telephone Cables, AJ.E.E. Trans., VoL 53, 274.
7. Overvoltages on Transmission Lines, AJ.E,E. Trans., Vol. 53, 1301.
8. Joint Use of Poles with 6900-volt Lines, AJ.E.E. Trans., VoL 52, 890.
9. Relay Handbook and Supplement, N.E.L.A., 1931.
10. N.E.L.A. Publication 118, Technical Theory of Inductive Coordination.
11. N.E.L.A. Publication 144, Some Features of Telephone and Telegraph Systems.
12. N.E.L.A. Publication 147, Cable Circuit Noise and Power Distribution Systems.
13. N.E.L.A. Publication 153, The Effects on Noise Frequency Induction of Grounded Neutral Generators.
14. N.E.L.A. Publication 212, Low-frequency Induction.
15. NJ2.L.A. Publication 239, Generator Wave Shape.
16. E.E.L Publication A-13, Power System Wave Shape.
17. Low-frequency Power Induction and Its Effect on D-c Telegraph Operation, presented at annual
meeting, Telegraph and Telephone Section, A.R.A., June 12r 1934.
18. Demonstration of Low-frequency Induction between Power and Telephone Circuits, also presented
at above A.R.A. meeting.
19. Cooperation is Kevnote in Rectifier Supply Coordination, by F. E. Sanford and V. G. Rettig,
Edison Elec. Inst. Bull, August 1935.
20. Earth Resistivity and Geological Structure, AJ.E.E. Trans., Vol. 54, 1153.
21. Measurement of Telephone Noise and Power Wave Shape, AJ.E.E. Trans., Vol. 54, 1307.
22. Engineering Reports of the Joint Subcommittees of the Edison Electric Institute and the Bell
Telephone System:
Vol. II, Report of Proj. Comm. No. 10, April 1932.
VoL II, Report 12, April 1932.
VoL II, Report 14, April 1932.
Vol. IV, Report 34, January 1937.
Vol. IV, Report 36, January 1937.
VoL IV, Report 38, January 1937.
VoL V, Report 41, January 1943.
VoL V, Report 44, January 1943.
VoL V, Report 45, January 1943.
Vol. V, Report 46, January 1943.
VoL V, Report 48, January 1943.
23. A.I.E.E. Committee Report, AJ.E.E. Trans., VoL 65, 417.
24. Provisional Report 24 (Technical Report 2G-2), A Study of Pole Strength in Jointly Used Poles, of
the Joint Subcommittee on Development and Research of the E.E.I, and B.T.S., Aug. 22, 1938.
25. AJ.E.E. Technical Report 47-82, Joint Use of Pole Lines for Rural Power and Telephone Sermcest
by J. W. Campbell, L. W. Hill, L. M. Moore, and H. J. Scholz, December 1946.
SECTION 11
ELECTRICAL MEASUREMENTS
FREQUENCY MEASUREMENTS
ART> BY WARREN A. HARRISON PAGE
1. Definitions 02
2. Using a Time Standard 04
3. Using a Frequency Standard 05
4. Employing Circuit Element Selectivity 11
5. Electromagnetic Phenomena 14
MEASUREMENT OF PRIMARY
ELECTRICAL QUANTITIES
BY J. G. FERGUSON
6. Measurement of Current 16
7. Measurement of Voltage 17
8. Resistance Standards 18
9. Capacitance Standards 20
10. Inductance Standards 22
11. Measurement of Resistance 23
12. Measurement of Capacitance and Con-
ductance 24
13. Measurement of Inductance and Effec-
tive Resistance 27
14. Signal Generators and Detectors 30
WIRE LINE MEASUREMENT
BY H. J. FISHER
15. Transmission Measurements 32
16. Noise Measurements 36
17. Cross-talk Measurement 37
18. Echo Testing of Lines 38
19. Square Wave Testing 39
20. A-c Bridge Method of Locating Irregu-
larities in Line Impedance 39
21. D-c and Low-frequency line Testing. . . 41
ROUTINE MEASUREMENTS ON A-M
AND F-M BROADCAST RECEIVERS
ART. -^T ^* O- SwiXYARD PAGE
22. Overall A-m Receiver Measurements. . . 43
23. Single-stage Measurements 48
24. Miscellaneous Measurements on A-m
Receivers 50
25. F-m Receiver Measurements 50
26. Overall Performance Tests 51
27. Single-stage Measurements 52
WAVE ANALYSIS
BY E. PETERSON
28. Wave Characteristics 54
29. General Analyzer Requirements 56
30. Methods of Wave Analysis 58
31. Spectrographs 65
MICROWAVE MEASUREMENTS
BY E. W. HotTQHTON
32. Impedance Measurements 70
33. Absolute Power Measurements 77
34. Attenuation Measurements 82
35. Frequency Measurements 84
SIGNAL GENERATORS AND POWER
MEASUREMENT
BY F. J. GAFFNEY
36. Oscillators for Signal Generator Use 89
37. Modulation of Signal Generators 93
38. Standardization of Output Power 96
39. Attenuator Design 99
40. Shielding Problems 101
41. Power Measurement 102
11-01
ELECTRICAL MEASUREMENTS
FREQUENCY MEASUREMENTS
By Warren A. Marrison
1. DEFINITIONS
By frequency is meant the number of times any periodic phenomenon recurs in a standard
unit of time. In general it is stated as^the number of complete vibrations, or oscillations,
or revolutions performed in 1 sec.
Occasionally other units of time are used, but usually they are specified so there is little
or no ambiguity. Thus, we speak of revolutions per minute. Sometimes tuning forks
are stamped DV or VS after the number designating the frequency. DV, which stands
for "double vibrations," means frequency as denned above, that is, the number of com-
plete periods per second, VS, which stands for "vibrations per second," designates twice
the true frequency.
The period of a cyclic or periodic phenomenon is the time duration of one complete
cycle. The rates of slow periodic phenomena are usually expressed in terms of the period.
For example, the period of a "seconds" pendulum is 2 sec.
Frequency may also be designated as angular velocity, especially in expressions repre-
senting the rate as a trigonometric function of time. Thus in expressions of the type
I = IQ sin (coi + a)
the constant, « = 2x/, may be considered as an angular velocity.
Frequency may be expressed in terms of wavelength when the velocity of wave propaga-
tion in a medium is assumed. This is most often used in discussions of electromagnetic
radiation where the velocity is approximately that of light, c = 2.998 X 1010 cm per sec.
The general relationship between frequency, velocity, and wavelength is
Velocity v
f (OT "> = Wavelength = X
A standard of frequency differs from most other working standards in that it is a rate
and cannot be represented completely by a physical body that can be preserved. Although
the frequency of a bar, or other simple shape, can be defined approximately for a given
mode of vibration in terms of its dimensions, density, elasticity, and coupling to other
bodies, the effects of these factors will not remain constant with as great accuracy as that
to which the resultant frequency can be measured in terms of astronomical time, that is,
in terms of the rate of the earth's rotation on its axis.
In the present system of measurements, the primary standard of frequency is the rate
of the earth's rotation, since all measurements of frequency are referred directly or in-
directly to the second of the cgs system which is by definition 1/86,400 of a mean solar day.
By the application of recently discovered atomic or molecular resonance phenomena to
the measurement of frequency and time it may be found possible eventually to place all
such measurements on a more nearly absolute basis, quite independent of the stability
of masses of matter such as now comprise the control elements in reference standards of
frequency and time, and independent of variations known to exist in astronomical time
itself. Some of these atomic and molecular resonance phenomena are in the range for
which continuous oscillations at ultra-high frequency may be produced by modern vacuum-
tube means, indicating the possibility of making frequency comparisons of high precision
throughout the entire range of continuous magnetic waves. The possibility of so using
these resonance phenomena was discussed by Professor I. I. Rabi in a talk before the
American Physical Society and the American Association of Physics Teachers in January,
1945.
The great importance of this impending development lies in the idea that the atomic
and molecular resonance phenomena, being properties of independent elementary particles
of matter, appear to be in certain cases completely independent of temperature, pressure,,
and other ambient conditions, which in various degrees affect the behavior of all existing
practical standards of frequency and time.
11-02
DEFINITIONS
11-03
Table 1. Some Useful Frequency Formulas
1. A-c generator with alternate N and S poles:
Inductor generator:
2. Electrical resonant circuit with L and C:
Same with L, C, and R in series:
3. Frequency of electromagnetic radiation (X = wavelength) :
/ =
No. of poles X rps
/ = No. of poles X rps
3.00 X 1010
X(cm)
Frequency of sound vibrations in any medium: /
4. If a condenser is charged to voltage E and completely discharged
/tunes a second into a current-measuring device: /
_ 1 /Y
X V
'oung's modulus
Density
Mean current
C X E
5. The period T of a simple pendulum with double amplitude = 29 : T = 2*"\ /- ( 1 -f sin2 - • • • I
\*\ 4 2 /
The frequency for small amplitude: / = — -V/l
Conical pendulum (angle B to vertical) :
Vertical pendulum (mass supported on spring) :
Torsion pendulum:
where rj, 1, and R are the torsion modulus, length, and radius of
the supporting member, and I is the moment of inertia, of the
6. Stretched string:
Overtones are 2/, 3/, etc.
7. Uniform rod, free-free, longitudinal:
Overtones are 2/, 3/, etc.
8. Uniform round rod, free-free, torsion:
Overtones are 2f, 3/, etc.
9. Long air column open at both ends:
7 = ratio of the specific heats.
Overtones are 2/, 3/, etc.
Long air column open at one end:
Overtones are 3/, 5/, etc.
10. Straight free-free bar in flexure:
k is radius of gyration of section.
Overtones are (5/3) 2/, (7/3) 2f, (9/3) 2/, etc.
Density
For flexural vibrations in generalt tuning forks, reeds, etc., having / =» K —^ A/— 5S* s m us
uniform section:
where K is a constant for a given shape and mode of vibra-
tion.
11. For any note in the equally tempered scale where n is the total f±n
number of semitones above (+) or below (— ) middle C.
(A = 440 cps.)
Exact frequency ratios between successive notes in the major
diatonic scale are: 9/8, 10/9, 16/15, 9/8, 10/9, 9/8, 16/15.
Density
220
12. Where I is the distance between nodes on Lecher wires or in
a coaxial conductor:
_._ 3 X 1010
2Z
11-04
ELECTRICAL MEASUREMENTS
The most accurate reference standards of frequency in use at present are vacuum-tube
oscillators whose frequencies are controlled by mechanical vibrators made of quartz
crystal. A special advantage of the oscillator type of standard is that its output of con-
stant-frequency current can be sent over suitable communication channels and used
anywhere as a reference standard of frequency. Such standards are maintained contin-
uously by the laboratories of the National Bureau of Standards, the Bell System, and
many others in America and abroad.
Oscillators of somewhat less accuracy have been built employing tuning forks or bars
of metal for the frequency-controlling element. Usually these are coupled to the vacuum-
tube circuit through electromagnetic means, but many such oscillators have been built
using magnetostriction and electrostatic attraction for the coupling means. Prior to the
general use of quartz for precise control, such oscillators were used in most frequency
standard installations. Now they are used chiefly where the advantage of direct low-
frequency control outweighs the requirement for extreme accuracy.
Although, for the greatest accuracy, frequency is defined and measured in terms of
astronomical time, preferably by means of a combined time and frequency reference stand-
ard, there are many cases in which a good estimate of its value can be made from a knowl-
edge of means controlling it or responding to it. Table 1 contains a number of formulas
that may be used for the approximate determination of frequency under a variety of con-
ditions.
Frequency measurements find their chief applications in electrical communication where
they are used in the study and adjustment of various oscillators and electrical networks
such as niters and equalizers. This applies in varying importance from the lowest frequen-
cies employed in d-c telegraph to the highest used in ultra-short-wave radio.
They are involved in the control of power frequencies and in certain time systems. They
are used in measuring linear and angular velocity and acceleration, for the study of vibra-
tion in mechanical systems, and for the most precise determinations of electrical-circuit
constants.
They are of ever-increasing importance in basic physical studies involving relations
between astronomical time, the velocity of light, and resonance phenomena in atoms and
molecules.
2. USING A TIME STANDARD
COUNTING. Since frequency is defined as the number of recurrences of a cyclic phe-
nomenon per unit of time, the most direct method of its measurement, and at the same
time the most precise, is to count the total number of cycles during a known time interval
and to divide by the number of elapsed seconds. The only inaccuracies in this method
are in determining the time interval and in estimating the number of cycles. If the time
error can be assumed to be negligible, and if the frequency is constant, the accuracy may
be increased to any extent by increasing the duration of the measurement.
Depending on the nature and the frequency of the phenomena to be measured, and the
accuracy required, the instrumentation may vary over a very wide range. For low fre-
quencies, and with relatively low accuracy, a stop watch may be used to count recurrences
over intervals of a few seconds. For greater accuracy, and for frequencies too high for
direct perception, some automatic registering or totalizing means is required. By means
of a chronograph or oscillograph, a recording
can be made of the recurrences during a speci-
fied time interval which may be analyzed at
leisure. By various counting means a continu-
ous total may be produced from which the fre-
quency may be determined with great accuracy
in any desired time interval.
SYNCHRONOUS CLOCK. This in effect is
the method used in calibrating the most accu-
rate frequency standards of the quartz-con-
trolled oscillator type. The actual method con-
sists in operating a synchronous clock from the
standard frequency source and in measuring
the rate of the clock in terms of observatory
time signals (astronomical time) by means of a
chronograph. Since the accuracy of individual
Fi<3. 1. Submultiple Generator of the Miilti-
vibrator Type. Capacitors C are for coupling
only.
time signals may be somewhat better than 0.01 sec, the day-by-day accuracy of this
method is of the order of 1 part in ten million. When the constancy of an oscillator
justifies the use of a longer interval between checks, the accuracy of determination may
USING A FREQUENCY STANDARD
11-05
be increased correspondingly. In this manner the rates of the best crystal oscillators
may be determined in terms of astronomical time with an accuracy better than 1 part
in a hundred million.
When accuracies of this order are involved, the variations in astronomical time itself
should be taken into account, since changes in the rate of the earth in excess of 1 part in a
hundred million have been observed from time to time. The largest such variation in
recent years occurred in 1918 and amounted to about 1 part in thirty million.
Since the frequency of a crystal oscillator, best suited for use as a precise frequency
standard, is too high to operate a synchronous motor directly, a circuit known as a sub-
multiple generator is used to _ ^
produce a frequency which is . >""' | 1 /and
an exact submultiple of the
original. Two or more stages
may be required, depending
on the ratio of the end fre-
quencies. In one system that
has operated continuously for
over 10 years, the ratios 5 X
Output
FIG. 2. Submultiple Generator of the Regenerative Modulator
Type
5X4 are used to operate 1000-cycle motors from a 100,000-eycIe primary standard. Simi-
lar means may be used to obtain frequencies in any range convenient for distribution or for
measurements which bear any exact rational relation to the primary control frequency.
Two of the more important means for frequency subdivision are illustrated in Figs. 1 and 2.
Although the former is most widely used, the latter has the advantage that no output is
produced in the absence of an input.
3. USING A FREQUENCY STANDARD
(Frequency Comparison)
Methods for frequency comparison may be divided broadly into two main classes:
those in which the actual number of cycles difference per unit of time may be determined
between the unknown frequency and some simple
exact fraction or multiple of the standard, and those
in which some approximation is used that does not
permit of actual counting. The first includes the va-
rious beat methods, the accuracy of which is limited
only by the stability of the sources and the duration
of observations. An accuracy of comparison of 1 part
in 1010 may be obtained by some of these methods
under good conditions. The latter includes (1) meth-
ods in which, for convenience and speed of operation,
a calibrated interpolation oscillator is used to interpo-
late between standard frequency values, (2) methods
FIG. 3. Balanced Vacuum Tube Mod- in which circuit selectivity, or other non-synchronous
ulator for Observing Low-frequency means, are used to indicate frequency in some part of
a the system, and (3) methods in which the frequency
of the source is in such a high range that the low-frequency beat contains irregularities
and cannot be treated as a sine wave and used in any direct counting procedure. The
accuracy of measurement in the last main class rarely ex-
ceeds 1 part in a million and may vary over a wide range,
depending on the particular apparatus used and the skill of
the observer.
ZERO BEAT. The simplest, most direct, and most accu-
rate methods are those for comparing two frequencies which
have nearly the same value. If the two sources are directed
into a modulator so that the low-frequency second-order
modulation produced goes through a d-c meter, the meter
reading will vary periodically at a rate which is the difference
between the two input frequencies. Thus the beats may be
counted over a suitable interval and the number per second
thus determined and added to or subtracted from the stand-
ard to obtain the unknown value. If the two frequencies are
alike, there is no response, hence the term "zero beat." Figures 3 and 4 illustrate typical
-modulator circuits useful for this method.
FIG. 4. Copper Oxide Modu-
lator for Observing Low-fre-
quency Beats
11-06
ELECTRICAL 3MEASUREMENTS
If a third-order modulator is used, such as silicon carbide, the greatest response is ob-
tained -with input frequencies near the ratio of 2 : 1. If higher-order modulation products
are used, as by overloading vacuum tubes or other modulators, appreciable response can
be obtained even when the input frequencies are related as m : n, provided that the product
of the integers m and n is not too great. In this case beats are obtained between the nth
harmonic of one input and the rath harmonic of the other. The numerical accuracy ob-
tained is proportional to the ratio of the actual beat frequency observed to the frequency
of the particular harmonic involved in the measurement. If the beat frequency obtained
in this way is too high to observe directly, other means may be used to determine it.
The accuracy obtainable by this general method may be very high. For example, if
the two frequencies, being in the ratio of nearly 1:1, are about 100,000 cycles, and if a
beat of about 1 cycle in 10 seconds is obtained, an accuracy of only 10 per cent in the
observed beat frequency corresponds to an accuracy of 1 part in ten million in the compar-
ison of the two high frequencies. Highly stable sources may be compared readily by this
means with an accuracy exceeding 1 part in 1010.
OTHER BEAT METHODS. If the beat frequency obtained from a modulator is too
high to observe directly, it may be measured by any other method suitable for the par-
ticular range encountered. For continuous comparisons the most precise method is to
operate a synchronous clock from the beat frequency and to compute the frequency from
its rate. A small percentage change in the rate of the undetermined high frequency will
cause a much larger percentage change in the rate of the clock. For example, if the stand-
ard were 100,000 cycles and the undetermined frequency in the neighborhood of 100,100
cycles, the multiplying factor would be 1000.
If merely an indication of moderate accuracy is required, without integrating or record-
ing, a commercial frequency meter, such as the vibrating-reed type, can be used giving a
direct reading accurate to 1 cycle or a little better. The beat frequency must of course
fall in the range of the particular instrument employed.
A very satisfactory direct-reading means for measuring the beat frequency in the range
from one cycle to about 200 cycles per second is illustrated in Fig. 5. The modulator
output operates a relay having a transfer con-
tact combination. A condenser with capac-
itance C is charged to voltage E at the beat
frequency / times per second. The meter
then reads / X C X E, which is directly pro-
portional to /. The factors C and E may be
chosen in relation to the sensitivity of the
meter so as to obtain a satisfactory scale
reading. For very low frequencies, either a
ballistic type of meter should be used, or a
filter should be included in the meter circuit,
in order to reduce meter fluctuation. Greater
FIG. 5. Direct-reading Beat Frequency Indicator accuracy may be obtained, at the expense of
the direct-reading feature, by balancing the
voltage across a resistor, used instead of the meter, against a fraction of the voltage E, thus
producing a null instrument. Both methods are suitable for continuous recording with
commercial sensitive d-c recorders and are capable of high overall accuracy.
Direct-reading instruments on the above principle have been built in which the relay
is replaced by electron trigger tubes in order to extend the usable range of the beat fre-
quency.
If the beat frequency is too high to measure accurately by any direct method, it can be
determined in terms of a lower standard frequency by using a second modulating stage.
This process can be carried out through a number of stages if desired so that, regardless of
the value of the original undetermined frequency, the final beat is low enough to be meas-
ured accurately by some direct method. In one method that has been worked out in
practice for measuring high frequencies, the frequency standard is made available in
multiples of 1,000,000 cycles, 100,000 cycles, 10,000 cycles, etc., so that, by successive
stages of modulation, a frequency determination is made in the range between 5000 and
30,000 kc in terms of a low-frequency beat and exact multiples of the several decade
standards.
The frequency range over which this principle may be applied is limited only by the
stability of the high-frequency oscillations. So long as the final beat frequency can be
measured as a continuous sine wave, the limiting accuracy is about the same as for the
zero-beat method. When, as is true at present of many ultra-high-frequency oscillators,
the final beat signal contains such random variations that the cycles cannot be actually
counted, some uncertainty enters even the best determinations of frequency. However*
USING A FREQUENCY STANDAKD
11-07
the accuracy may still be very high, because the beat frequency can be made such a very
small part of the total range, thus reducing the necessity for great accuracy in its measure-
ment.
STROBOSCOPIC METHODS. Stroboscopic methods are used for comparing the
rate of one mechanical rotation or vibration with another or with the frequency of a fluc-
tuating source of illumination. They are essentially low-frequency methods but have
been used to measure speeds of rotation in excess of 10,000 rps. The accuracy of compar-
ison is limited only by the constancy of the rates involved and the duration of a measure-
ment, being in that respect like the beat methods just discussed.
In general a means is provided for permitting an observer to see an object periodically
for very short intervals of time. If the object has a periodic structure like gear teeth or
spokes, and if in the interval between glimpses it rotates a distance equal to one or any
whole number of elements, it will appear to be stationary. If the glimpse frequency is
not exactly equal to the apparent
periodicity in the rotating struc-
ture, it will appear to move slowly,
the amount and direction of mo-
tion corresponding to the relative
rates. The time required for an
apparent motion of the structure
equal to one element space may be
considered as the duration of one
"beat" and treated as such in the
comparison of rates. This method
can be used in a large number of
ways for measuring or comparing
rotation speeds or for measuring
frequency in terms of known rota-
tion speeds, or vice versa.
A simple apparatus for either
case consists of a neon or other va-
por lamp which can be flashed pe-
riodically by pulsating current, and
a disk such as shown in Fig. 6 hav-
ing concentric rows of black and
white sectors of different periodic-
ity, attached to a suitable rotating
mechanism. If properly chosen,
one row of sectors will appear sta-
tionary or nearly so in the intermittent illumination, and from the observation the
ratio of the rotation speed to the flash frequency can. be deduced readily and with great
accuracy.
Similarly the frequency of any mechanical vibration of sufficient amplitude can be
determined by observing the motion with a light flashed at a frequency that can be ad-
justed to the proper range. If the flash frequency is adjusted to the highest value that
will give a single image of the vibrating part, that is the desired frequency, which can
then be measured by electrical means or read from a calibrated dial.
CATHODE-RAY OSCILLOSCOPE. Probably the most useful of aH laboratory
apparatus for frequency comparison is the cathode-ray oscilloscope, now available in
many compact and convenient forms. (See also Section 15, article 23.)
The oscilloscope, illustrated in Fig. 7, consists of a device for producing a stream of
electrons which is directed toward a fluorescent screen within an evacuated tube, and of
means for deflecting the electron beam in accordance with currents or voltages to be
studied, thereby moving the luminous spot on the screen. At ordinary frequencies the
motion of the spot is so rapid that its path is indicated by a continuous trace,
In the usual form of tube the deflections are obtained electrostatically by applying
voltage to pairs of parallel electrodes between which the electron beam passes. When two
voltage waves are to be compared they are connected to the two pairs of mutually perpen-
dicular plates corresponding to the x and y axes in a cartesian coordinate system, j The
resulting motion of the spot on the screen is such that
. 6. Stroboscope Disk (Courtesy of General Radio Co.)
x =
-f-
y = &eo sin (a$ -f <ps)
where k is a constant for the tube and where e, co, and <p are the voltage, angular velocity,
and phase corresponding to the input waves.
11-08
ELECTRICAL MEASUREMENTS
The actual figure that is traced can be determined analytically in simple cases by elim-
inating t between the two equations. For example, if ei = ez, «i = «2, and <& — <pi = ?r/2,
Electron
Bearr
_
-/7nrzr>-
m
• J
Fio. 7. Schematic of Carfiode-ray Oscilloscope, Illustrating Electrostatic Method for Obtaining
lissajous Figures
we get x2 4- y2 = &V, which is the equation of a circle. As the angle ((pz — <pi) changes
we get various phases of an ellipse until, when it becomes 0 or TT, it degenerates into a
straight line inclined 45° to the axes. Thus when two waves are compared having equal
amplitude and nearly equal frequencies, the pattern goes through a complete series of
ellipses once for each cycle gained or lost by one frequency on the other. One such cycle
Phase Angle
Musical
Internal
90°
135°
Dnlson
Octave
Octave and Fifth
Frequency
RaiTo
1.1
2.1
3.1
3.2
Fourth
FIG. 8. Typical Lissajous Figures with Corresponding Frequency Ratios and Musical Intervals
of pattern changes corresponds to one "beat" between the input frequencies. Measuring
the frequency of recurrence of such beats provides a convenient and extremely accurate
comparison between the input frequencies.
Patterns formed in this way by frequencies that are equal or related as m I n, where m
and n are integers, are known as Lissajous figures. Several such figures corresponding to
simple frequency ratios and different
phase angles are shown in Fig. 8.
When frequencies are to be com-
pared which differ by a rather large
ratio, say 10 : 1, a figure is obtained
such as shown in Fig. 9. The figure
looks like the projection of a sinusoidal
trace of 10 cycles around a transparent
cylinder. For illustration only, the
drawing shows half of the figure solid,
FIG. 9. Ten-to-one Lissajous Figure
corresponding to the front side of the hypothetical cylinder, and the remaining half dotted.
Actually, as viewed on the screen these two parts are indistinguishable in appearance.
If the ratio departs very slightly from 10 : 1, the pattern moves as though the hypothetical
USING A FREQUENCY STANDARD 11-09
cylinder rotated slowly at the rate of 1 complete revolution for every cycle gained or lost
at the low frequency. Thus when the part shown solid in Fig. 9 moves to the right,
the part shown dotted moves in the opposite direction.
In order to avoid the confusion of this double pattern, most cathode-ray oscilloscopes
are- now equipped with sawtooth wave sweep circuits, the frequency of which may be
precisely controlled by an external standard. By this means the back pattern is eliminated
and the whole visible pattern stands or moves as a unit.
Sometimes it is desirable to compare frequencies bearing a large ratio such as 100 ' 1,
or even 1000 : 1, in order to study small departures from such ratios, determined by other
means, or to adjust the frequencies to those exact ratios. The patterns corresponding to
such large ratios are too complex to be used in determining them directly, but by means
of an auxiliary oscillator of intermediate frequency it is easy to obtain a nearly exact
adjustment in two or three stages. For example, the 100 : 1 setting can be obtained by
means of an auxiliary oscillator having 10 times the lower of the two frequencies concerned.
As soon as the approximate adjustment is obtained between the end frequencies, the inter-
mediate oscillator can be dispensed with and the final comparison carried out with the
large ratio pattern. In such a procedure the horizontal gain of the oscilloscope may be
made so large that only part of the complete figure appears on the screen. Because of the
enlargement of the figure obtained in this way the accuracy of observation is materially
improved. This is essentially a zero-beat method permitting extreme accuracy of com-
parison.
Frequencies over a very wide range may be compared by the cathode-ray-oscilloscope
method, since many oscilloscope tubes will produce clear figures with inputs from the
lowest frequencies up to many megacycles. The interpretation of multiline figures corre-
sponding to fractional ratios and many special methods for using the oscilloscope are
described in the references.
AUDIBLE METHODS. Audible methods are often useful, especially as a means for
observing in one of the various beat methods. For example, if two frequencies which are
nearly alike can be heard simultaneously, the beat frequency may be sensed as variations
in loudness. The beats may be counted in order to determine the departure of one fre-
quency from the other, or one of the frequencies can be adjusted to match the other by
listening for zero beat. If one or both of the sound sources is rich in harmonics other ratios
than 1 i 1 may be studied readily by this means.
When two audible frequencies are nearly alike and one source is movable in actual
location, it is sometimes convenient to use the Doppler effect to determine which one is
high. For example, if an observer holds a vibrating tuning fork in a stationary sound
field of nearly the same frequency, slow beats will indicate the magnitude but not the sign
of the frequency difference. However, if, while still vibrating, the fork is moved away
from the observer and the beat frequency becomes lower (while moving) , the fork fre-
quency is higher than that of the sound field.
Often the musical pitch sense may be used to advantage in comparing the actual pitch
of two tones one of which may be considered as standard. Since a musical semitone is
approximately 6 per cent, it is evident that by this means alone the ratio of two tones in
the musical range may be estimated to well within 5 per cent. As a direct measurement,
this accuracy is insufficient for most purposes, but it is good enough to be very useful in
making estimates of beat frequencies between two high-frequency sources. For example,
a 5 per cent error in the 500-cycle beat between two frequencies, nominally 25 megacycles,
corresponds to an error of only 1 part in a million in their comparison.
As an aid to this method it is convenient to keep in mind that the frequency ratios
corresponding to the consecutive pairs of notes in the major diatonic scale are:
9 10 16 9 10 9 16
8 9 15 8 9 8 15
The product of all these together equals 2, that is, an octaxe. Also the product of the
first four equals 3/a, that is, the musical fifth, and similarly for the other recognized musical
intervals.
Most keyboard musical instruments are tuned to the equally tempered scale in which the
interval corresponding to all semitones is equal to V 2, and a whole tone equals two semi-
tones. In Table 2 the actual frequencies are listed for a range including that of an 88 note
piano with A above middle C equal to 440 vibrations per second. This is the most generally
accepted standard of musical pitch. For the convenience of using round numbers, a pitch
system is sometimes specified in which all the C's are powers of 2, middle C being 256
vibrations per second. The frequencies in this scale are about 2 per cent lower than in
the accepted standard of musical pitch, corresponding to about a third of a semitone. The
11-10
ELECTRICAL MEASUREMENTS
Table 2. Equally Tempered Scale A = 440
C4-C3
Cr-C2
CrOi
Ci-C
C-C'
C'-C2
C2-C3
C3-04
c
16.35
32.70
65.41
130.81
261.63
523.25
1046.5
2093.0
c#
17.32
34.65
69.30
138.59
277.18
554.37
1108.7
2217,5
D
18.35
36.71
73.42
146.83
293.66
587.33
1174.7
2349.3
D*
19.45
38.89
77.78
155.56
311.13
622.25
1244.5
2489.0
B
20.60
41.20
82.41
164.81
329.63
659.25
1318.5
2637.0
F
21.83
43.65
87.31
174.61
349.23
698.46
1396.9
2793.8
F#
23.12
46.25
92.50
185.00
369.99
739.99
1480.0
2960.0
G
24.50
49.00
98.00
196.00
392.00
783.99
1568.0
3136.0
G#
25.96
51.91
103.83
207.65
415.30
830.61
1661.2
3322.4
A
27.50
55.00
110.00
220.00
440.00
880.00
1760.0
3520.0
A£
29.14
58.27
116.54
233.08
466.16
932.33
1864.7
3729.3
B
30.87
61.74
123.47
246.94
493.88
987.77
1975.6
3951.1
C
32.70
65.41
130.81
261.63
523.25
1046.50
2093.0
4186.0
PIG. 10. Frequency Comparison
with Interpolating Oscillator
latter pitch is used chiefly in physics and sometimes is known as physical pitch. Inter-
national pitch is based on A = 435.
INTERPOLATION METHODS. Most measurements of frequency, apart from the
inter comparison of standards and similar studies, can be made most expediently, and with
sufficient accuracy, by the use of a calibrated interpolating oscillator in combination with
some means such as just described for indicating exact frequency relationships. The
principle is illustrated in Fig. 10, which may be modified or extended in numerous ways
depending on the application. It is evident that other types of indicator than oscilloscopes
could be used, and that by means of suitable switches,
JSi and $2, only one indicator is needed for the simple
example described in the following.
The operation is best explained by an example. Let
the standard be 100,000 cycles, and let us determine a
frequency, say 3,564,000 cycles, by means of an inter-
polating oscillator stable in the range from 500,000 to
600,000 cycles and having a vernier dial, FL, calibrated
in this range. By a little experimenting one finds readily
that an integral 6 : 1 pattern is observed on oscilloscope
B when the interpolating oscillator is set a little below
600,000. That is the cue to calibrate the interpolating
oscillator at 600,000 in terms of the standard by setting
the dial to that exact value and adjusting vernier V$
(which adjusts the frequency slightly, independently of
FI) until the ratio of the pattern on oscilloscope A
is exactly 6:1. When the oscillator is again adjusted to give a 6 1 1 stationary pattern
on oscilloscope B, the dial reading multiplied by 6 will be the frequency to be determined.
In general it is best to so calibrate the interpolating oscillator that the two positions on
the calibration dial are as near together as possible. When the oscilloscope is the indicator
it is often desirable to use multiline figures in making one or both settings in order to accom-
plish this. For example, if the unknown frequency bore some simple ratio to 533,000
cycles, the three line pattern corresponding to the ratio 5 lfo should be used in calibrating
the interpolating oscillator. It is evident that the overall accuracy of the general method
may be increased materially by this means especially if an auxiliary vernier dial is provided
which is calibrated in a small percentage range and which can be used to interpolate be-
tween two close settings.
The method illustrated in Fig. 10 may be used in setting the "unknown" frequency at
any value P X Q times the standard, where P and Q are integers or simple rational frac-
tions. Using stationary figures on both oscilloscopes simultaneously, the accuracy of
setting is very high. The * 'unknown" frequency can then be used as standard in a wide
choice of frequencies to extend the range. Sometimes it is convenient to use more than
one interpolating oscillator when it is necessary to cover a wide range of frequencies.
In particular this method can be used for extending the frequency of a standard upward
for the purpose of measuring at ultra high frequencies in the decimeter and centimeter
range. As yet, however, the oscilloscope cannot be used to obtain observable Lissajous
figures at the highest frequencies because the stability of such oscillators is not yet good
enough to produce stationary figures. This may be expected to come with time, however,
and already cathode-ray tubes have been produced capable of resolving single traces at
frecjueaeies as high as 10,000 megacycles.
EMPLOYING CIRCUIT ELEMENT SELECTIVITY 11-11
For ultra-high-frequency measurements in terms of a standard the usual method is to
heterodyne a harmonic of a measurable source, such as the "unknown" of Fig. 10, -with
the high frequency by means of a crystal detector and either to estimate the frequency
of the relatively low-frequency components obtained or to change the variable source until
the detector output is as near to zero frequency as can be estimated. This does not have
to be actually zero to be good; it should be remembered that, when measuring 10,000
megacycles, corresponding roughly to 3-cm waves, 10,000 cycles in the beat corresponds to
only 1 part in a million in the overall measurement.
Standards of frequency of very great accuracy are made available by the National
Bureau of Standards through continuous radio transmissions from station W WV. All
the carrier frequencies, which are 2.5, 5, 10, 15, 20, 25, 30, and 35 megacycles, are regu-
lated by the primary frequency standard of the bureau. Each carrier is modulated with
seconds pulses and with the audio frequencies 440 and 4000 cycles, also of very high
accuracy.
4. EMPLOYING CIRCUIT ELEMENT SELECTIVITY
When extreme accuracy is not a primary requirement, or when standard-frequency
current is not available, it is often convenient to measure frequency in terms of the response
of selective electrical networks or mechanical resonators.
METERS FOR POWER FREQUENCIES. Most of the commercial meters for indi-
cating power frequency operate on one of three principles. Meters of the reed type employ
a number of reeds tuned consecutively to slightly different values and loosely coupled to
an electromagnet energised by the current to be measured. The reeds whose frequencies
-i -
v
J-> ^v ^
J J
t »
\
1
1
A.C.
\
1 Input
I
I
V
One Reed""i
in Vibration '
'&AVW
58
59
60
1
61
1
62
1
Appearance of Scale
When Indicating
Frequency of Input
FIG. 11. Vibrating-reed Frequency Meter
correspond most nearly to the frequency of the input current vibrate at the largest ampli-
tude. Usually the reeds are arranged in a row, as shown in Fig. 11, with the ends in line
near a scale so that the frequency of the reed with greatest amplitude can be read oft
directly. Such meters are available in a considerable range of frequencies and are very
useful for measuring low frequencies directly or for indicating beat frequencies in their
range.
The Weston frequency meter, shown in Fig. 12, has a movable soft-iron armature free
to move in the resultant field from two mutually per-
pendicular coils. When the frequency has some nomi-
nal value, the fields in the two coils are equal and the
armature takes up a nominal position parallel to the
resultant field. When the frequency changes, the
ratio of currents in the coils changes,
owing to the frequency selectivity of
the input circuits, causing a shift in
the resultant field and a correspond-
ing movement of the armature.
The induction frequency meter,
shown in Fig. 13, consists essentially
of two opposing induction voltmeter
elements associated with one arma-
ture. The two motor elements are
suppled through resistive and reac-
tive circuits respectively so that the
ratio of the effective currents varies
with the applied frequency. In the type of meter shown, a circular disk is used and the
indicating position, is that for which a restoring spring just balances the resultant torque
FIG. 12. Weston
Frequency Meter
13 induction Frequency Meter
11-12
ELECTEICAL MEASUREMENTS
from the opposing drive elements. The deflection is therefore proportional to the frequency
deviation from a nominal value.
In another type of this meter no restoring spring is used, but the armature is so shaped
for one or both motor elements that the torque varies with angle of deflection as well as
with input current. This permits an angular balance position to be obtained which does
not depend upon the applied voltage or the reaction of a spring.
Some meters for power frequencies employ resonance to increase the sensitivity in a
narrow frequency range. These and others are described in standard works on power
meters.
BRIDGE METHODS. Various bridge methods may be used for measuring frequency.
The one shown in Fig. 14 is typical. The bridge is balanced when,
With head phones, or other suitable null indicator, the frequency can be measured in
terms of Rit R%, Ci, and CV As a frequency meter two of these elements can be made
variable and calibrated to read input frequency at
balance. For more detail about bridge measuring
devices see below, article 12.
THE MONO CHORD. This is a useful labora-
tory tool for the approximate determination of fre-
quency in the lower and medium audible ranges.
It consists of a steel wire under tension between
movable bridges, the wire being coupled electro-
magnetically to the a-c input to be measured. The
frequency of maximum response can be determined
from the constants of the system, or a calibration
can be made in terms of length or tension. Under
FIG. 14. Bridge for Measuring Frequency some conditions an accuracy of 1 part in 1000 may
be obtained with this means.
RADIO WAVEMETER. The tuned circuit wavemeter, Fig. 15, used extensively for
radio-frequency measurements from 10 kc to 100,000 kc, consists primarily of a coil and
condenser connected in a closed circuit and loosely coupled to~ a source to be measured.
The circuit is tuned, usually by means of the condenser, until a resonance condition is
indicated. From a scale on the condenser, previously calibrated by means of accurately
known input frequencies, the frequency of any source in a limited range can be read off
directly. In commercial wavemeters of this sort a set of coils is generally provided suitable
for use in a number of adjacent and somewhat overlapping ranges.
The coupling from the source to be measured may be effected (1) through a low im-
pedance, such as a low resistance, in series with the tuned circuit; (2) by loose magnetic
coupling; or (3) by loose capacitance coupling as indicated in Fig. 15.
Resonance may be indicated (1) by a current-indicating instrument, such as a thermal
galvanometer, in series with the timed circuit; (2) by a voltage-indicating instrument, such
as a crystal detector or diode in
parallel with the reactive elements
(if the source is modulated by au-
dio frequency, head phones may
provide the most convenient means
for observing) ; (3) by the reaction
on a power-indicating means asso-
ciated with the source; (4) by a
measure of power in a separate
aperiodic circuit coupled to the
7
Shield'
FIG. 15. Radio Wave Meter. Resonance type with high
impedance resonance indicator.
tuned circuit but not directly to
the source; and (5) by means of
amplification followed by detection
as in a simple radio receiver.
Although all five methods are used, the fifth is preferable because of the vanishingly
small effect of the indicating means on the Q of the tuned circuit and hence on the precision
of observation. Used as indicated, an effective Q of 500 may be attained in a good part
of the range, and with good equipment and careful procedure an accuracy of the order
of 1 part in 104 may be achieved.
QUARTZ RESONATORS. Specific frequencies may be indicated with great accuracy
by means of quartz resonators coupled loosely across the tuning elements of a resonant
wavemeter. Owing to the relatively very much higher Q of the crystal, which is often in
EMPLOYING CIRCUIT ELEMENT SELECTIVITY 11-13
excess of 100,000, its response characteristic is confined to a correspondingly narrow and
well-defined range of frequency. This response characteristic is superposed on the broader
characteristic of the tuned circuit. Used in this way such resonators are valuable chiefly
in fixing calibration points on the wavemeter. A variable input can be adjusted until
the crystal response is indicated; then, with the same input frequency, the wavemeter
condenser can be adjusted for maximum response to fix the calibration at the.frequency
of the crystal.
Quartz crystals may be used in a great variety of ways as single-frequency indicators.
One interesting adaption, due to Giebe and Scheibe, consists of a series of resonators
mounted in a gas at low pressure which may be coupled electrostatically to a circuit to
be tested. If a frequency is applied which corresponds to that of one of the resonators,
the large potential gradients in the neighborhood of that resonator due to its resonance
will cause a luminous discharge which serves as indicator. This method is somewhat
analogous to the reed indicator but is applicable to frequencies up to a million cycles per
second or more and of course is inherently much more accurate.
CAVITY RESONATORS. The most convenient and generally satisfactory means for
measuring frequencies in the region from 200 to 30,000 megacycles has been cavity
resonators, which have been developed in a variety of forms for different frequency ranges
and for different methods of use. A cavity is primarily an almost completely enclosed
space in a rigid piece of metal, with openings only for coupling electromagnetic energy
from wave guides or coaxial conductors, and usually also for the operation of a plunger
for frequency adjustment.
The cavity itself in its lowest-frequency modes may be considered a familiar tuned
circuit in which the capacitance is formed by opposite sides, sometimes the two flat ends
of a cylinder, and connected by a continuous array of single-turn coils forming the cylinder
wall. It is evident that for a moderate-sized cavity the effective capacitance and induct-
ance are both very small and hence the frequency is very high. Since there are no radiation
losses, and since the interior losses may be kept small, the Q factor may be very high. For
silver-plated fixed cavities the Q may exceed 20,000; for adjustable cavities it is somewhat
less.
Cavities are resonant elements and as such may be used as selective transmission devices
indicating a maximum of transmitted energy into a detector, or as selective absorption
devices indicating a minimum in a high-impedance source. In either case the actual
detection is most easily accomplished by a crystal detector which may actuate a d-c meter,
or, if the source is modulated, a set of head phones may be used, with amplification if
necessary. The setting accuracy may be as high as 1 part in 105.
The design, construction, and use of cavity resonators are discussed at length in Section
7 and in references.
TRANSMISSION LINES. Very high frequencies can be measured with fair accuracy
by a study of standing waves in transmission lines, the three usual types being Lecher wires,
coaxial conductors, and wave guides. The simplest method involves a movable short-
circuiting conductor which can be moved along the line by external control, and the ob-
servation of successive minima due to reaction on the source of high-frequency energy fed
into the line. The actual distance between successive positions of the short-circuiting
conductor which causes such minima determines a half wavelength for the particular line
used. In the case of Lecher wires (parallel wires a few centimeters apart) and coaxial
lines, the frequency is given approximately by
3 X 1010
• 2Z
where I equals the distance between resonance positions. A calibrated instrument based
on this method may be accurate to about 0.1 per cent.
Although Lecher wires are convenient for purposes of demonstration, a low-resistance
lamp on the short-circuiting rider being a suitable indicator of resonance, the attainable
accuracy is limited by large radiation losses, especially at high frequencies. Wave guides
are inconvenient for this purpose on account of the wide variety of modes that may give
false indications unless special precautions are taken to suppress them. High-frequency
transmission lines are discussed in Section 10, and some of the accompanying references
deal with their use as frequency-measuring devices.
THE ECHELETTE GRATING. A method, closely analogous to the familiar optical
grating, has been developed for establishing the frequency of the shortest electromagnetic
radiations producable experimentally. The method consists in directing the radiation in
question toward an array of stepped metal reflectors, like the slats in a Venetian blind, and
in observing the angle of reflection for which the greatest intensity of reflected energy is
obtained. From the spacing of the reflectors, and the measured angles for maximum
11-14
ELECTBICAL MEASUREMENTS
energy, the wavelength may be computed with considerable accuracy as with the optical
grating. This method of measurement, in fact, was an important step in establishing the
continuity of the electromagnetic spectrum between light produced by thermal excitation
and electric waves produced by purely electrical means.
5. ELECTROMAGNETIC PHENOMENA
Table 3 shows in a graphical manner the relation between the frequencies of various
observed electromagnetic phenomena. Where any considerable uncertainty exists as to
the extent of a range due to ambiguity of definition or due to disagreement among sources,
the uncertainty is indicated by dotted extensions.
Table 3. Frequency Spectrum of Electrical Phenomena
Cosmic rays
Q&Ql A-s-
1 x-imli
1 angstrom ttnit
Sodium D Fines
Highest frequency produced electrically
Highest frequency continuous wave
National Bureau of Standards
Standard frequency transmissions — j
2.5, 5, 10, 15, 20, 25, 30, and 35 Me L
MiddJeC
Seconds
radl-afiOQ
produced electrically
ommercial radio
ndard broadcasting
-- Audible range
l telephone
j- Audible rang
rComrnercial
1QJ^_ |
» 1 n5 — !
D-c telegraph
The lower end of the chart, and extending a little beyond 3 X 1010, includes the entire
range over which continuous alternating current can be produced at the present tune.
This is also the entire range over which frequencies can be measured or compared directly.
Damped waves having frequencies up to 3 X 1012 have been produced by purely electrical
methods. In this region, which overlaps the infrared spectrum, the frequencies can be
determined by either electrical resonance methods or by optical interference methods.
From 1Q12 upwards the terms on the right refer to electromagnetic waves originating in
hot or otherwise luminous bodies, in excited atoms, or in atom nuclei. Between 1012
and 1Q20 the frequencies are calculated from measured wavelengths; from 10s* upward
they are calculated from measured photon energies. In certain ranges either of two names
is applicable, as indicated by the overlapping grouping.
It is interesting to note that, by extendiing the frequency spectrum downward, frequen-
cies of recurring astronomic phenomena are encountered that are about as far removed
from onje cycle as are the highest frequencies noted. Thus the frequency of rotation of
tibe earth on its axis is 1.16 X 10~5; the frequency of revolution of the earth around the
SOB is 3.17 X 10"8. The frequency of rotation of the equinoxes around the ecliptic is
BIBLIOGRAPHY 11-15
1.2 X 10""12. The frequency of rotation of Andromeda Nebula is estimated (Jeans) to
be 1.7 X 10~15, and it is perhaps reasonable to suppose that frequencies of periodic phe-
nomena involving interactions between the nebulae may be many orders smaller. Thus
the frequencies to which the senses respond most readily are, on a logarithmic scale, about
midway between the extremes of which we are aware.
BIBLIOGRAPHY
Books
Jansky, Cyril M., Electrical Meters, McGraw-Hill, 1917.
Pierce, George W., Electric Oscillations arid Electric Waves, McGraw-Hill, 1920.
Brown, Hugh A., Radio Frequency Electrical Measurements, McGraw-Hill, 1931.
Hund, August, High Frequency Measurements, McGraw-Hill, 1933.
Brainerd, J. G., Kochler, Glen, Reich, Herbert J., and Woodruff, L. F., Uttra High Frequency Tech-
niques, D. Van Nostrand, 1942.
Montgomery, C. G., Technique of Microwave Measurements (Rad, Lab. Series 11), McGraw-Hill, 1947.
Articles
Cady, W. G., The Piezoelectric Resonator, Proc. I.R.E., Vol. 10, No. 2, 83-114 (April, 1922).
Nicols, E. F., and Tear, J. D., Short Electric Waves, Phys. Rev., Vol. 21, Series II, 587-610 (June 1923).
Pierce, George W., Piezoelectric Crystal Resonators and Crystal Oscillators Applied to the Precision
Calibration of Wave Meters, Proc. Am. Acad. Arts and Sci., Vol. 59, No. 4, 81-106 (October 1923).
Hund, August, Theory of Determination of Ultra-radio Frequencies by Standing Waves on Wires,
Scientific Papers of Bureau of Standards No. 491 (June 23, 1924).
Giebe, E., and Scheibe, A., Leuchtende piezoelektrisehe Resonatoren als Hochfrequenznormale,
E.T.Z., Vol. 47, 380-385 (April 1926).
Oapp, J. K., Universal Frequency Standardization from a Single Frequency Standard, J.Q.S.A. and
RJSJ., Vol. 15, No. 1, 25-47 (July 1927).
Rasmussen, Frederick J., Frequency Measurements with the Cathode-ray Oscillograph, J". AJ.E.E.,
Vol. 46, 3-12 (July 1927).
Allen, George E., The Accuracy of the Monochord as a Measurer of Frequency, Phil. Mag,, Vol. 4,
Series 7, 1324-1337 (December 1927).
Ferguson, J. G., and Bartlett, B. W., The Measurement of Capacitance in Terms of Resistance and
Frequency, Bell Sys. Tech. J., VoL 7, 42(M37 (July 1928).
Pierce, George W., Magnetostriction Oscillators, Proc. I.R.B., Vol. 17, 42-88 (January 1929).
Marrison, W. A., High Precision Standard of Frequency, BeU Sys. Tech. J., July 1929, pp. 493-514,
Proc. I.R.E., July 1929, pp. 1103-1122.
Marrison, W. A., A Method for Estimating Audible Frequencies, Bell. Lab. Rec., Vol. 8, No. 4, 178-
182 (December 1929).
Polkinghorn, F. A., and Roetken, A. A., A Device for the Precise Measurement of High Frequences,
Proc. I.R.E., VoL 19, 937-948 (June 1931).
Johnson, J. B.r The Cathode-ray Oscillograph, J. Franklin Inst., Vol. 212, No. 6, 687-717 (December
1931).
Loomis, Alfred L., and Marrison, W. A., Modern Developments in Precision Clocks, Trans. AJ[JBJS.f
June 1932, pp. 527-537.
Peterson, H. O., and Braaten, A. M., The Precision Frequency Measuring System of R.C.A. Communi-
cations, Inc., Proc. I.R.E., Vol. 20, No. 6, 941-956 (June 1932).
Mickey, L., and Martin, A. D., Development of Standard Frequency Transmitting Sets, Bur. Standards
J. Research, Research Paper 630 (January 1934).
Dye, D. W., and Essen, L., Valve Maintained Tuning Fork as Primary Standard of Frequency, Proc.
Royal Soc., January 1934, pp. 285-306.
Forbes, H. C., and Zaugbaum, F., Frequency, Time Control with Telephone Aid, Elec. World, Jan. 20,
1934, p. 117.
Seheibe, A., und Adelsberger, U., Die technischen Einrichtungen der Quarzuhren der Physikalisch-
Technisehen Reichsanstalt, Eoch frequenztechnik und Elektroakustik, February 1934, Band 43,
Heft 2, pp. 37-47.
Hazen, Grace, and Kenyon, Frieda, Primary Radio-frequency Standardization by the Use of the
Cathode-ray Oscillograph, Scientific Papers of Bureau of Standards, No. 489 (May 1934).
Williams, Emrys, Audio-frequency Measurement by the Electrically Excited Monochord, Proc. LR.E.,
VoL 22, No. 6, 794-804 (June 1934).
Cleeton, Claud E-, Grating Theory and Study of the Magnetostatic Oscillator Frequency, Physics,
June 1935, pp. 207-209.
Cleeton, C. E., and Williams, N. H., The Shortest Continuous Radio Waves, Phys. Rev., VoL 50,
1091 (December 1936).
Essen, L., and Gordon-Smith, A. C., The Measurement of Frequencies in the Range 100 mc/s to 10,000
mc/s, J. I.E.E., Part III, Vol. 92, No. 20, 291-295 (December 1945). _
Jones, William J., Types and Applications of Microwave Frequency Meters, Radio, January 1946,
pp. 29-34.
Clayton, R. J., Houldin, J. E., Lamont, H. R. L., and Wilkshaw, W. E., Radio Measurements in the
Decimeter and Centimeter Wave Bands, J. I.EJB.t Part III, Vol. 93, No. 22, 97-117 (March 1946).
Lee, Gordon M., A Three4>eam Oscillograph for Recording at Frequencies up to 10,000 Megacycles,
Proc. I.R.E., and Waves and Electrons, VoL 34, No, 3, 121W-129W (March 1946).
Essen, L., Cavity Resonator Wave Meters, Wireless Engineer , VoL 23, No. 272, 126-132 (May 1946).
Booth, C. F., and Laver, F. J. M., A Standard of Frequency and Its Applications, J. I.E.K, Part III,
Vol. 93, No. 24, 223-236 (Jury 1946).
GafFney, F. J., Microwave Measurements and Test Equipment, Proc. I.R.S., and Waves and Elec-
trons, VoL 34, No. 10, 775-793 (October 1946).
Lafferty, J. M.t A Millimeter-wave Ueflex Oscillator, J. Applied PAy*., VoL 17, No. 12, 1061-1066
(December 1946),
Marrison, W. A., Tke Evolution of tbe Quartz Crystal Clock, B&.TJ., VoL 27, 510-588 (July 194S).
11-16
ELECTRICAL MEASUREMENTS
MEASUREMENT OF PRIMARY ELECTRICAL QUANTI-
TIES (CURRENT, VOLTAGE, RESISTANCE,
CAPACITANCE, AND INDUCTANCE)
By J. G. Ferguson
The primary quantities of interest in the communications field may be divided into two
classes: first, current and voltage; and second, the so-called circuit constants, resistance,
capacitance, and inductance. Power is usually obtained from the measurement of voltage
or current, and resistance. Frequency is covered under Frequency Measurements, pp.
11-1 to 11-15.
Values of current and voltage generally do not require very accurate measurement.
On the other hand, very severe requirements are justified economically in the design and
measurement of circuits and their component parts if they result in an increase in the
number of channels which can be made available from a given physical circuit. These
requirements are specified for the most part in terms of the three circuit constants, re-
sistance, capacitance, and inductance.
The frequencies of interest in communication circuits range from a few cycles per second
to the super high frequencies used in radio transmission, whereas the frequency range of
major interest from the standpoint of the measurement of primary circuit constants is
from about 30 cycles to about 100 megacycles.
6. MEASUREMENT OF CURRENT
The values of power of interest have a lower limit of about 10 ~16 watt determined by
the necessity of keeping a level above resistance noise, and an upper limit of about 1 watt
in wire transmission, determined by the necessity of avoiding excessive cross-talk to other
circuits. The upper limit, of course, is considerably higher in certain applications such
as radio transmitters. The currents corresponding to these power limits for the impedance
ranges encountered range from about 0.1 amp down to fractions of a microampere. The
three features most desired in an instrument to measure such currents are : an impedance
practically non-reactive and independent of frequency and current level, a method of
operation which furnishes effective values, and high ratio of response to input power.
TYPES OF INSTRUMENT. The dynamometer type and the magnetic-vane type
measure effective values of current but require high input power. They are seldom used
except at power frequencies. Practically all a-c measurements of current use as an in-
dicator a d-c instrument of the moving coil-permanent magnet type. The problem then
reduces to a means of transforming the alternating current to direct current.
THE THERMOCOUPLE TYPE. This has an impedance which is practically a pure
resistance at all frequencies, and it measures effective values of current. It is the most
accurate method for the measurement of small currents because it can be calibrated with
reversed direct current. Its principal disadvantages are that, irrespective of the current
measured, the output power is low, about 1 microwatt, and it will not stand heavy over-
loads. Enclosing the couple in a vacuum improves its speed and sensitivity and reduces
temperature errors. The usual type has a heater in direct contact with the junction.
This gives a maximum sensitivity and speed and is satisfactory for all but the highest
frequencies. At very high frequencies the direct contact between the a-c and d-c circuits
introduces objectionable couplings between the instrument and other parts of the circuit.
A type having the couple insulated from the heater is to be preferred above about a million
cycles in spite of a somewhat slower speed and slightly lower efficiency.
Typical vacuum couples of either the insulated or contact type have a couple resistance
of about 10 ohms and are designed to work into a microammeter having a resistance of
about the same value and a full-scale deflection of 200 to 300 jua. Table 1 gives essential
information for instruments of this type having various ranges. Their accuracy is usually
Table 1. Typical Ranges and Resistances of Thermocouple Instruments
Range,
milli-
amperes
Input
Resistance,
ohms
Range,
milli-
amperes
Input
Resistance,
ohms
Range,
milli-
amperes
Input
Resistance,
ohms
250
100
50
0.5
2.0
4.0
25
10
7
10
35
50
5.0
2.0
1.5
100
600
1000
MEASUREMENT OF VOLTAGE 11-17
about 1 per cent of full-scale reading when used with the couple with which they have been
calibrated.
Multirange milliam meters are made with self-contained shunts. The accuracy of such
instruments at high frequencies is usually limited by the shunts.
Contact Rectifier Type. Contact rectifiers used in conjunction with d-c meters are the
most rugged and efficient of the various low current instruments. The most common type
uses the copper vs. copper-oxide disk. These instruments have the disadvantage, common
to all rectifiers, that they introduce modulation due to instantaneous variation of the input
resistance with current. This may be reduced considerably by the common arrangement
of four units in bridge form, or an equivalent arrangement with two units and a center
tapped transformer. They usually measure more nearly average than effective values,
thus giving a wave-shape error. Their principal disadvantages lie in the variation of the
rectification properties with time and temperature and the fact that the input impedance
varies with current and has a large capacitive component which acts as a shunt across the
rectifier and renders their use above about 10,000 cycles of little value, unless some com-
pensation is provided. With proper compensation their frequency range may be extended
considerably. For higher frequencies silicon or germanium crystal rectifiers may be used.
Since different ranges can be obtained by changing either the size of the disks or the
sensitivity of the d-c meter, a very wide current range is available. It is possible to obtain
meters with a full scale as low as 100 ^ta, but their resistance is high, about 3000 ohms.
This makes them suitable for voltmeters, which can be obtained with ranges as low as
0.5 volt with a resistance of 3000 ohms per volt.
The accuracy of this type of instrument is usually limited to about 5 per cent of full
scale, and errors in excess of this may occur with extremes of temperature and wave shape.
Two-element vacuum-tube rectifiers have characteristics somewhat similar to contact
rectifiers. They are satisfactory up to much higher frequencies but have the disadvantage
of requiring auxiliary power. They are discussed further under voltmeters.
MEASUREMENT OF HIGH CURRENT VALUES. These measurements may be
made by means of low-range meters in conjunction with current transformers or shunts.
Shunts are preferred for high frequencies. They should be designed to have impedance
characteristics similar to those of the meter, particularly when used at high frequencies,
so that the current will divide in the same proportion at all frequencies.
MEASUREMENT OF LOW CURRENT VALUES. Measurement of current values
below the range of even the most sensitive instruments can be made after amplification by
comparison with a known current obtained by attenuating a measured current a definite
amount.
7. MEASUEEMENT OF VOLTAGE
With the high impedances almost inevitable in an instrument for measuring low current
values, there is no marked distinction between the measurement of current and voltage;
thus all the methods discussed for current measurement will also measure voltage. How-
ever, care must be taken to avoid errors due to impedance change caused by series reactance
in the leads at high frequencies. Static voltmeters are also common. They measure
effective values, but their low sensitivity and high input capacitance limit their use to
comparatively high voltages and low frequencies. In addition the following are available.
VACUUM-TUBE RECTIFIERS. This type provides the most satisfactory means of
voltage measurement. Most vacuum-tube voltmeters employ diode rectifiers with high-
resistance loads, rather than triodes, since the indication is less dependent on the tube
characteristics, and because plate-voltage variations, which are a source of error in the
triode, are eliminated,
To measure low voltages the rectifier is either preceded by an a-c amplifier or followed
by a d-c amplifier. The frequency range and sensitivity of the former are limited by the
problem of obtaining broad-band stabilized amplification. Instruments are available in
multiple-range models with sensitivities in the order of 1 millivolt, covering the frequency
range of 20 cycles to 5 megacycles. The input impedance is in the order of 0.5 megohm
shunted by a few micro-microfarads. Indicated voltages are usually average values.
The sensitivity of diode voltmeters is limited by the diode characteristic, and the
frequency is limited principally by lead inductance. To reduce this error, the diode is
usually encased in a small probe connected to the set by a cable. Instruments are available
in multiple-scale models with sensitivities of 0.1 volt covering the frequency range of 20
cycles to 100 megacycles. Input impedance is usually 1 megohm or more at low frequency
but is limited at high frequency by the capacitance and conductance of the diode, which
may be as high as 7 wi and 10 micromhos at 10 megacycles. Indicated voltages are usually
half wave peak values.
11-18 ELECTRICAL MEASUREMENTS
The accuracy of vacuum-tube voltmeters is 2 to 5 per cent, depending on wave shape and
frequency.
For frequencies above the range of the diode, materials of high temperature coefficient
of resistance are used in which the voltage is determined by the resistance change due to
heating. Owing to their small size they may be made independent of frequency up to
several thousand megacycles.
8. RESISTANCE STANDARDS
For the accurate measurement of circuit constants, precision standards are required.
They form the most important part of the measuring circuits and therefore require full
consideration. They consist of resistance, capacitance, and inductance. The following
discussion is limited to their use as standards. Further general information can be found
in Section 3.
Resistance standards are usually wire wound, but high resistances are also made by
coating a thin film, usually of carbon, on an insulating form. These films have a high tem-
perature coefficient of resistance, about — 0.03 per cent per degree centigrade for carbon,
and cannot be adjusted to very close limits. They are fairly stable with time if hermetically
sealed, and the change with frequency is small for values below 10,000 ohms. They are
cheaper than wire wound, especially for high resistance values.
The types of wire used most generally for resistance standards are the copper-nickel
alloy Constantan and the copper-nickel-manganese alloy Manganin. Both materials have
very low temperature coefficients, the variation in resistance over the temperature range
of ordinary use being well below 0.005 per cent. Constantan is more easily soldered, and
its resistance is more stable with time. Manganin is preferred for d-c standards on account
of its lower thermoelectric power to copper, but this is a minor consideration for a-c use.
Both alloys have a specific resistance of about 30 times that of copper. Other alloys con-
taining chromium or iron have higher specific resistances but are not generally used on
account of their higher permeabilities and larger temperature coefficients.
EFFECT OF HUMIDITY. Humidity affects the distributed capacitance of resistance
windings unless they are sealed or impregnated. The impregnating material is usually a
thin solution of shellac or a wax, such as paraffin. Impregnation also serves to prevent
change in shape of the support or spool, but it is desirable to use as a support a material
impervious to moisture, such as a suitable plastic, ceramic, or glass. The woven type of
wire standard is the most independent of changes in the form.
PHASE ANGLE. The phase angle should be small. It is due to inductance, distributed
capacitance, and capacitance between the terminals which is not due to the presence of the
winding. Inductance can be reduced by reducing the size of wire and by winding the coil
BO that adjacent turns have opposite directions of winding and are spaced as close together
as possible. Minimum spacing is determined by the thickness of insulation. Therefore,
for a given type of wire and insulation there is a definite mininiuni obtainable ratio of
inductance to resistance for any given wire size, this value being reduced as the wire size
is reduced. Distributed capacitance can be reduced by winding so that turns which are
adj acent physically are consecutive electrically. By this means the distributed capacitance
can be reduced below the remaining capacitance between the terminals. Both types of
capacitance can be decreased by reducing the physical size, that is, by reducing the wire
size. Capacitance and inductance, when both are present in a resistance, have a com-
pensating effect. For the small reactances present in resistance standards, the compensa-
tion will be almost perfect at all frequencies if the relation L = Cr2 holds.
The reactance of carbon film type standards may be considered due entirely to capaci-
tance between terminals. This may be held to about 1 ppf. .
VARIATION WITH FREQUENCY. Resistance change with frequency is due prin-
cipally to the presence of skin effect and of residual reactances. Skin effect may be reduced
by using a small size of wire and reducing the inductance of the winding by suitable choice
of winding type. For non-inductive windings, the increment due to skin effect may be
taken as less than 0.1 per cent for No. 28 B.&S. gage wire at 1 megacycle, and less than 1
per cent for No. 30 wire at 10 megacycles. Where power considerations do not enter,
sizes smaller than these are generally used in order to reduce the phase angle as already
discussed, and skin effect is therefore usually negligible.
Reactance is a more serious cause of resistance variation with frequency. If a resistance
has inductance in series with it, the effective resistance component of the combination
eonsidef ed as a parallel circuit will be increased to the value r + (bPLP/r) - If the resistance
feas capacitance in parallel with it, the effective resistance of the combination considered
as a series circuit will be decreased to the value r — o^CV. When both inductance and
RESISTANCE STANDARDS
11-19
capacitance are present, the value of resistance is a function of both, and, if the
inductance and capacitance are in such proportions as to give it a zero phase angle, its
value will be increased to r -f- (<*rL?/r). For high resistances at high frequencies, the
dielectric loss of the associated capacitance affects the resistance value.
TYPES OF WINDINGS. The following windings are suitable for resistance standards
having values above about 50 ohms, for which cases the reduction of both inductance and
capacitance is important:
The Curtis winding made by winding one turn around a spool, then passing the wire
through an axial slot and winding the next turn in the opposite direction. A flat slotted
form or card is an improvement over a round spool.
The inductive winding on a thin flat card.
The woven type in which the warp consists of silk or cotton threads and the weft is the
resistance wire.
The Ayrton-Perry type consisting of two parallel opposed windings either in a single
layer, in which case they must cross at every turn, or one layer wound over the other. The
single layer has a little more capacitance and a little less inductance than the two layers.
For resistance below 50 ohms where capacitance has less effect, windings having greater
distributed capacitance such as the bifilar, and the reversed layer type may be used.
A well-made unit using No. 36 B.&S. gage wire may be wound to have a ratio of react-
ance to resistance, due to inductance, of about 0.1 at I megacycle, and, using No. 44 wire,
to have a ratio of about 0.2 at 10 megacycles. If the capacitance is such as to give zero
phase angle, which it may for windings of about 1000 ohms, the corresponding resistance
increment will be about 1 and 4 per cent respectively. If the capacitance value is not such
as to give zero phase angle, the effective shunt resistance will be different from the effective
series resistance.
Table 2 gives representative values of inductance and capacitance for standards of
several values wound with various sizes of wire.
Table 2. Representative Resistance Windings
Inductance and capacitance for various values and wire sizes
Resistance,
ohms
Type of Winding
Insulation and
Wire Size
B.&S. Gage
Residuals
Net Residual
L,fb
c,
w*f
I/, ;ih
C' = £'/r2,
fifd
0.1
1
10
100
100
100
100
1,000
1,000
1,000
1,000
10,000
10,000
10,000
Bifilar, tape
Bifilar, tape
Bifilar
Bifilar
Curtis (card)
Ayrton-Perry (2 layers)
Woven
Reversed layer
Ayrton-Perry (2 layers)
Woven
Curtis (card)
Reversed layer
Ayrton-Perry (1 layer)
Woven
0.004 in. X 0.1 25 in.
0.004 in. X 0.063 in.
33 DSC
S6DSC
40 DSC
40 BE
40 BE
39 DSC
44 BE
44 DSC
40 DSC
42 DSC
44 DSC
44 DSC
0.01
0.04
0.16
0.8
0.4
0.35
0.30
4.2
2.5
2.0
4.0
30
25
20
0.01
0.04
10
80
0.5
1
!
24
1
0.5
1.5
20
2
0.5
0.16
0
0.4
0.34
0.29
-20
1.5
1.5
2.5
0
-40
-34
-29
20
-1.5
-1.5
-2.5
20
1.8
0.3
VARIABLE STANDARDS. Variable standards are used in precision measurements
principally for covering the range between the smallest steps of the adjustable standards.
They are usually wire wound and of low range. The simple series type has the abjection
that the contact resistance is usually an appreciable part of the total resistance of the
standard. Preferred methods are to use the slide wire in a circuit as a potentiometer, in
which case the contact resistance is not in the measuring circuit, or to use a shunted type
of slide wire, in which case the resistance of the slide wire itself is higher than the range
of the combination, thus reducing the effect of the contact resistance. Inductance con-
stitutes the principal frequency limitation. The shunted type has lower inductance than
the potentiometer type but does not have a linear scale unless used as a potentiometer.
Compensation for inductance in single-turn slide wires may be made by substituting an
equivalent length of copper wire for the resistance wire removed from the circuit. Com-
pensation in the wound type is not generally made but can be effected in special eases by
winding the slide wire non-inductively.
High-resistance variable standards are sometimes used in shunt connection as low-grange
conductance standards. These are commonly a composition type, particularly when used
at high frequencies. They are not very stable standards.
11-20
ELECTRICAL MEASUREMENTS
Resistor
ADJUSTABLE STANDARDS. Adjustable standards consist of a number of switch
assemblies, usually 1 to 6, each containing resistance units arranged to give values in steps
from 1 to 10. The switch and wiring add both inductance and capacitance. These may
be reduced by reducing the switch size
and the amount of dielectric material in
it. These requirements are met very
well by the wafer-type switch. The
small size introduces some difficulties in
obtaining satisfactory low and stable
contact resistance, but the introduction
of silver contacts reduces this difficulty.
Their principal objection is their short
life. They have considerable flexibility
due to the availability of multiple decks.
The usual arrangement is to connect 10
equal resistances in series and to short-
circuit those not in use by means of the
brush. The ground or low-potential side
of the circuit should be connected to the
brush to minimize the effect of capaci-
tance. The inductance may be compen-
sated for by using an additional 10 studs
as shown in Fig. 1, to insert inductance
equal to the inductance of the resistance
and wiring which is removed, thus keep-
ing the total circuit inductance constant
for all switch settings at the cost of a slight increase of the zero inductance. This arrange-
ment uses 2 decks of a wafer switch.
A method which reduces both capacitance and inductance to a minimum, and is there-
fore suitable for both high and low resist-
ances, is shown in Fig. 2. A 20-stud switch is
so arranged that the drum supporting the
units and studs rotates, the brushes remain-
ing stationary. Each unit in a decade has a
resistance equal to the total value required for
that particular setting. There is no switch
wiring and there are no coils connected when
not in use. The short-circuit connection for
the zero setting may consist of a copper strap
equal in inductance to the mean value of the
units. The same arrangement with station-
ary studs and moving brushes is almost as
satisfactory and allows the use of a 2-deck
wafer switch. The principal disadvantage is
the necessity for 10 different values for the
resistance units.
For high resistances there are advantages
in arranging decades to read conductance.
This means connecting them in parallel.
Compensating
Inductor Brushes
FIG. 1. Decade Resistance Standard, Compensated
for Inductance
100 ohm decade
FIG. 2. Rotor Type Decade Resistance Standard
Four units of value 1, 2, 3, 4 can be connected in various parallel combinations. The
switching arrangement is the same as that for switching capacitors, shown in Fig. 5A.
9. CAPACITANCE STANDARDS
The principal requirements for a capacitance standard are a capacitance independent
of time, humidity, temperature, voltage and frequency; a low power factor; and small
size. The degree to which these requirements can be met depends principally on the choice
of dielectric. All capacitors using solid or liquid dielectrics have losses when subjected to
alternating voltages. The equivalent circuit of such a capacitor may be indicated as shown
in Fig. 3 as a perfect capacitance C either with a resistance rs in series with it, or with a con-
ductance g in parallel with it. For these networks to be equivalent the two capacitances
are not identical, but for the low power factors of standards, the difference is negligible.
i. Practically the only dielectrics used for capacitance standards are mica or air. Many
other solid dielectrics are used for capacitors. None of them combines all the advantages
CAPACITANCE STANDARDS
11-21
a> CB>
FIG. 3. Alternate Equivalents for an Im-
perfect Capacitor. A, parallel equivalent;
B, series equivalent.
of mica, although polystyrene is equal or superior to mica in practically all respects except
temperature coefficient of capacitance.
Mica capacitors may be made of interleaved sheets of mica and foil such as copper, tin,
or aluminum, or by depositing a film of metal, usually silver, directly on the mica. The
last has the advantage of eliminating any air film between the dielectric and the metal,
making the capacitance less dependent on the
mechanical stability of the assembly. c
Air capacitors require solid dielectric in their j 1 I r c
construction. Their performance depends consid- ' l • j r*
erably on their design as well as on the dielectric. 1 I VW\>
STABILITY WITH TIME AND HUMIDITY. L/ys/^J
All capacitors change slightly with age, owing to " — —
structural changes after assembly; good mica
capacitors usually increase less than 0.05 per cent
with age. Humidity has a serious effect unless
the capacitors are protected. They are usually
dried and hermetically sealed, either in molded
plastic or in a can. In addition they may be vacuum-impregnated, usually with paraffin
or Superla wax. Well-made air capacitors are less subject to these changes.
VARIATION WITH TEMPERATURE. The change in capacitance with, temperature
of mica capacitors is due partly to the dielectric material but is also affected considerably
by the mechanical design. Unimpregnated capacitors usually have a positive linear
change, which is due primarily to changes in the physical dimensions. In impregnated
capacitors, additional changes occur owing to the effect of the wax, which has a negative
temperature coefficient that increases with temperature. As a result, the temperature
coefficient of the capacitor depends on the amount of wax and may be made extremely
small over a limited temperature range. Standards can be obtained which vary less than
0.05 per cent from 10 deg cent to 35 deg cent. The shunt conductance of all mica capacitors
increases with temperature. The amount varies considerably, but an average value may
be taken as 2 per cent per deg cent. For air capacitors capacitance change is due partly
to the insulating supports but principally to change in the plate area and spacing caused
by changes in the dimensions of the parts. It may be reduced by the choice of materials
of low temperature coefficient of expansion and by avoiding distortion due to unequal
expansion of the parts.
VARIATION WITH FREQUENCY. Variations in capacitance with frequency of mica
standards are caused by variations in the dielectric constant, and at high frequencies by
the effect of inductance in the leads. The former causes a slight decrease in capacitance
with increasing frequency, the change being approximately logarithmic with respect to
frequency. The latter causes an increase in capacitance equal to oo^LC2. Lead inductance
in a good standard may be held below 0.05 juh. Air capacitors change less, because of
the smaller amount of dielectric material and because their comparatively low capacitance
is affected by lead inductance only at higher frequencies.
An imperfect capacitor may be represented as shown in Fig. ZA or Fig. 3B. Metallic
losses constitute a series resistance which is independent of frequency, except for skin
effect. Leakage constitutes a shunt conductance independent of frequency. Dielectric
loss is of such a nature that the loss per cycle is proportional to capacitance and approxi-
mately independent of frequency. In other words, this loss is proportional to &C. If
represented by Fig. 3A, g will be
TaWe 3. Loss Variation with Frequency and directly proportional to frequency,
Capacitance and if represented by Fig. 3£, rs
will be inversely proportional to
frequency.
In general, four different quan-
tities are in common use for indi-
cating the quality of a capacitor
from the standpoint of loss. These
are series resistance r, shunt con-
ductance g, power factor which
when small is equal to the dissipa-
tion factor coCV or g/&C, and the
reciprocal, which is commonly termed Q. Table 3 indicates how these quantities vary
with frequency and capacitance.
In this table D is a fundamental property of the dielectric and is approximately inde-
pendent of the frequency. For good mica it is as low as 0.0001 and decreases slightly with
increasing frequency.
Source of Loss
r
Q
P.F.
g
Series resistance r,
ra
I
r&C
r^-C*
Dielectric, D > .
D
1
T\
«C
D
D-c leakage go
So
uC
SO
go
03 C2
£0
wC
11-22
ELECTRICAL MEASUREMENTS
Low power factor or high Q in a standard is obtained by choice of mica of low dielectric
loss, by keeping lead resistance low, and by eliminating moisture and impurities in assem-
bly. Figure 4 shows curves of power factor and Q in terms of frequency for representative
standards. The increase in Q with frequency is a characteristic of the dielectric. The
decrease at high frequencies is due
to effective series resistance. The
larger the value of capacitance, the
lower is the frequency at which the
maximum, occurs. Small capaci-
tance values usually have greater
dielectric loss because of the greater
influence of the sealing material.
They also have greater effective
series resistance, owing, in part at
least, to the smaller number of
sheets in parallel.
The Q of air standards is usually
higher than that of mica on ac-
count of the reduced dielectric ma-
terial and the reduced effect of
series resistance due to the smaller
capacitance.
30 100
Frequency in kilocycles
300
1000
PIG. 4. Variation with Frequency of Q of Typical Mica
Capacitor Standard
VARIABLE STANDARDS. Variable standards are practically always air capacitors.
They may be considered as two capacitances in parallel, one consisting of the Tnirnmum
capacitance which includes the dielectric material, and the other consisting of the variable
part. The former may be considered as a fixed capacitance shunted by a conductance
representing the dielectric loss, which is not a function of setting. The latter may be
considered as a loss-free variable capacitance in parallel with the former. They may be
used, therefore, in measuring circuits, to obtain loss-free changes hi capacitance. On the
other hand, considering the standard as a whole, the power factor increases with decrease
in setting and may be greater than that of a mica capacitor at minimum setting unless a
very low loss dielectric is used.
ADJUSTABLE STANDARDS. These are usually in decade form, but, owing to the
cost of good standards, only 4 units are gener-
ally used, the switch connecting them in the
parallel combinations necessary to obtain steps
from 1 to 10. Practically all such switches re-
duce to the principle of a brush for each unit
contacting successively 10 studs which are
wared so as to connect the unit in circuit at the
positions required to give the desired combina-
tions. This may be most readily done with
minimum wiring by using cams. The method
is indicated by the developed cam arrangement
shown in Fig. 5.4. . By using 2 brushes on dif-
ferent diameters a single cam may be cut to
connect 2 units. Wafer switches can. be used
requiring only 2 cams and 5 brushes mounted
on a single deck to perform the whole switching o 1 2 3 4 5 6
sequence. A similar switch may be mounted on A senes connection
the same shaft with cams cut inversely as fiq- 5. Cam Type of Decade Switch for
, • -n- EI> i. * 71 T * j * • Senes or Parallel Connection of 4 Standards,
shown in Fig. 5B but parallel-connected to an- A, parallel connection; B, series connection,
sert capacitances in place of those removed
to compensate for the capacitance of the switch or for that of the units in excess of
nominal values.
10. INDUCTANCE STANDARDS
The requirements for inductance standards are similar to those for capacitance stand-
ards, namely, high stability of inductance under all operating conditions, low power factor
or high Qt and small size. Coils cannot be built to meet these requirements as well as
capacitors, and for this reason they are not used to the same extent as standards. For
precise standards no magnetic material is sufficiently stable, and air-core coils are almost
aNrays used. They are wound either as toroids or as solenoids. The toroids have tees
external field but are larger for the same performance. External field is objectionable
MEASUREMENT OF RESISTANCE 11-23
since it not only causes errors in measurement due to coupling to the rest of the circuit
but the inductance of the standard itself is affected also. Shielding is generally used con-
sisting of magnetic material at low frequencies and low-resistance material such as copper
at high frequencies.
STABILITY WITH TIME AND HUMIDITY. Coils may be constructed to have
negligible change in inductance and resistance with time. They are usually sealed and
in addition may be impregnated to eliminate humidity effects.
VARIATION WITH TEMPERATURE. Change in inductance is determined prin-
cipally by mechanical changes in the form and in the impregnating material when present.
By choice of materials of low expansion these changes can be held to as low as 0.001 per
cent per deg cent. A single-layer solenoid wound under tension on a ceramic form may
be made with a temperature coefficient of less than 2 parts per million per deg cent.
Change of resistance is due principally to change in the resistivity of the copper winding
and to change in eddy-current loss which in turn is due to the change in resistivity. These
changes are of opposite sign. The net change is a function of frequency but is usually
positive.
VARIATION WITH FREQUENCY. Variations of inductance and effective resistance
with frequency are due principally to eddy currents and distributed capacitance. The
former results in an increment of resistance which is proportional to the square of the
frequency. It can be reduced by using stranded wire and single-layer windings. The
effect on the inductance is usually negligible compared with other effects. Distributed
capacitance has the effect of increasing both inductance and effective resistance. It is a
minimum for single-layer coils. Where this type is impractical, banked or sectionalized
windings may be used. Capacitance to ground can be reduced appreciably only by reduc-
ing the size of the coil, which is at the cost of Q. For frequencies well below the resonant
frequency of the coil, the increment in inductance due to capacitance C is w^C, and the
increment in the effective resistance is 2co2LCr. The dielectric conductance g associated
with the distributed capacitance may also be appreciable. It increases the resistance of
the coil by gcJL*. If the coil has no appreciable resistance or inductance variation with
frequency, then the ratio of reactance to resistance or Q is proportional to the frequency.
On the other hand the loss due only to capacitance and eddy currents results in a Q in-
versely proportional to the frequency. For the actual case, the Q usually increases to^a
maximum and then decreases. For low frequencies a high Q can be obtained only by means
of a large size. This is the principal disadvantage of air-core standards. It is most evident
when they must be used for measuring magnetic-core coils. As the frequency increases
the comparison becomes more favorable to the air-core coils on account of the increase in
core loss and decrease in effective permeability of magnetic core coils. Above 100 kc this
disadvantage is negligible, and air-core coils can be built of sma,ll size to have values of Q
as high as 100 to 200.
INDUCTOMETERS. All inductometers have an appreciable stray magnetic field
which may cause error due to magnetic coupling to other parts of the circuit. They have
characteristics similar to fixed standards but usually have relatively greater capacitance
and greater resistance increment. The inductance and resistance increments are a func-
tion of the setting as well as of frequency.
One type consists of two coils arranged so that the position of the field of one may be
varied so as to change their mutual inductance. They may be used as variable mutual
inductors or, by connecting the two windings in series, as variable self-inductors. Another
type consists of a single-layer rotating solenoid with spaced bare wire turns and a fixed
brush riding on the turns. The former type has the advantage of no sliding contacts, but
the latter has better performance in other respects.
ADJUSTABLE STANDARDS. Coils may be assembled to form adjustable standards
similar to resistance and capacitance standards. Because of their large size, poorer char-
acteristics, and difficulty in compensating for capacitances of switch and wiring with series
connection, they are not used extensively. A typical method of connecting 4 units to
form a decade is shown in Fig. 5.5. Additional decks with cams cut inversely may be
used to insert compensating resistances in place of inductances removed.
11. MEASUREMENT OF RESISTANCE
The method used almost exclusively for measuring circuit constants is the bridge method
in which the unknown quantity is compared with a standard of known value. For the
higher frequencies, say, above 10 megacycles, the errors caused by the presence of even
very small stray inductance or capacitance limit the range and flexibility of the bridge
11-24
ELECTRICAL MEASUREMENTS
method, and consequently at these frequencies other methods which involve less apparatus
and simpler circuits are also used.
Resistance standards can be made so that their effective resistance does not differ from
the d-c value appreciably compared with the errors of measurement up to the maximum
frequencies used- Accordingly, the measurement of resistance is usually made by direct
comparison with,a standard on a bridge. The simplest type is the equal ratio-arm bridge.
A modified equal ratio-arm bridge useful for the a-c mea-
surement of both resistance and phase angle is shown in
Fig. 6. It is adaptable only to the measurement of re-
sistors having small phase angles, but, with a given air
capacitor Cb of small range across one ratio arm, it will
measure the reactance of resistors of any value over a
wide frequency range. The equations of balance for
this bridge for resistors of small phase angle are
/-r
Cx
T
or Lx
and
FIG. 6. Bridge Circuit for Measure-
ment of Resistance and Phase Angle
of Resistora
where r, is the resistance of the standard.
rx, Cx, and Lx are the values for the unknown.
Both positive and negative reactance can be measured
by either transposing the standard and unknown in the
bridge or by transferring the capacitance Cb from EC
to AB. If the standard has appreciable reactance, cor-
rection for it is necessary. For maximum accuracy the
bridge should be shielded. A method of shielding simi-
lar to that shown in Fig. 8 is satisfactory.
At very high frequencies a direct substitution in a resonant circuit as described under
"Measurement of Inductance" may be used, or a voltmeter-ammeter method, with a
vacuum tube voltmeter and a thermocouple.
Calibration of standards for phase angle may be made by substitution of one resistance
by another having the same physical configuration but a different resistance value, thus
obtaining a change in resistance without changing the associated inductance or capaci-
tance. For low resistances this may be done by making identical standards of copper and
of various resistance alloys. For high resistances, carbon of different thickness may be
deposited on identical forms.
The measurement of effective resistance associated with inductance and capacitance is
considered under those headings.
12. MEASUREMENT OF CAPACITANCE AND CONDUCTANCE
TYPES OF CAPACITANCE. In practice, a capacitor does not usually consist of a
single capacitance between two terminals. There is, in addition, capacitance to ground or
to other objects. The capacitor is usually equivalent to
a three-terminal network of three capacitances even when
reduced to its simplest form. As a result, different values
of capacitance will be obtained, depending on the condi-
tions of measurement. Referring to Fig. 7, Ci is the ca-
pacitance to ground from A, and C$ is the capacitance to
ground from B. The direct capacitance between A and B
is C; the mutual capacitance is C + CiC^/(C\ + Cs) ; and
the grounded capacitance is C -f- Ci or C + Cz, depending
on whether B or A is grounded. Any or all of these ca-
pacitances may require measurement.
In actual use, the capacitor is generally connected either
from one side of the system to ground, in which event it
is a grounded capacitance which is effective, or directly
FIG. 7. Simplified Network of Ca-
pacitor Which Has Capacitance to
Ground
across the system which is balanced to ground, in which event it is the mutual capacitance
that is effective. Direct capacitance is required, in general, only for special purposes or
where the capacitor is so connected in service that the three direct capacitances are
connected across different parts of the circuit and must be known individually.
BRIDGE METHODS OF MEASUREMENT. Owing to the satisfactory characteristics
01 capacitance standards, the measurement of capacitance is usually made by direct com-
MEASUREMENT OF CAPACITANCE AND CONDUCTANCE 11-25
parison with them. The simplest and most accurate method is the equal ratio-arm bridge.
The advantages of this type of bridge over all other types are that the equality of the
ratio arms may be tested in the bridge itself by means of simple reversal, and residual and
lead impedances may be more readily balanced because of the symmetrical arrangement.
The ratio arms are usually resistances. Capacitances have advantages for high voltages,
and inductances, particularly when closely coupled, for high currents. For precise work,
especially at the higher frequencies, some method of taking care of undesired capacitances
between arms and from the arms to ground is necessary, the best method being to shield
the bridge. This shielding should include at least one transformer. The shield should be
complete enough to reduce the direct capacitance between windings below 1 /i;xf- In
special cases it should be much better than this.
Capacitance. Figure 8 shows a shielded equal ratio-arm bridge which is satisfactory
for the measurement of capacitance by
direct comparison with a standard.
This bridge will measure mutual,
grounded, and direct capacitance. The
requirement that must be met in order
to measure mutual capacitance is that
the bridge corners C and D be balanced
to ground. Since there is no capacitance
to ground from B, and since A and C
are at the same potential when the
bridge is balanced, this requirement is
met when the total capacitance from A
and C to ground equals the capacitance
from D to ground. If at the same time
these capacitances are proportioned to
keep the bridge in balance, then the ca-
pacitances from A and C to ground will
be equal, each being half the capacitance
from D to ground. This adjustment
may be made by means of auxiliary air
capacitors. Grounded measurements
are made by grounding the D corner by
switch Ki. If the bridge is limited to
grounded measurements, D may be per-
manently grounded, and the double shielding of the transformer
is unnecessary.
Conductance. The loss in a capacitor may be measured as a series resistance or as a
shunt conductance. Using the bridge of Fig. 8 a standard resistance may be connected
either in series or in parallel with the standard capacitor to balance this loss. For wide
ranges of capacitance and power factor, however, the range of resistance required in either
case is objectionable. The series method may require excessively small resistances, and
the shunt method may require excessively high resistances. A modification which permits
of a practical resistance range is to shunt both arms by a resistance of fairly high value
and to reduce the resistance across the standard to balance any loss in the capacitor under
test. Satisfactory values are 10,000 ohms for the fixed resistance across CD and a variable
resistance range from 0.01 ohm to 10,000 ohms across AD. This allows the measurement
of conductances from 0.0001 micromho up. If TO is the reading of r*n in ohms for the zero
balance and ri is the reading with the capacitor in circuit, then
FIG. 8. Completely Shielded Equal Ratio-arm Bridge
Suitable for Balaneed-to-groimd or Grounded Measure-
ments
and the ratio arms
gx
mhos
If TO is approximately 10,000 ohms, and the conductance is below 1 micromho T this
reduces to
gx
. ,
microrahos
The bridge then becomes practically direct reading for conductance. This approxima-
tion holds for conductance values encountered in all good standards at moderate frequen-
cies. These expressions are actually the difference in the loss between the standard and
the capacitor under test. If the standard has conductance, it must be added to the
difference obtained.
In order to calibrate standards for conductance, it is necessary to have a primary stand-
ard of zero or known conductance. This is usually obtained by means of an air capacitor
specially designed to give a direct capacitance having no loss. If an air capacitor is built
11-26
ELECTKICAL MEASUREMENTS
so that each set of plates is mounted by insulating supports on a third metal conductor
or shield, we then have a system of three capacitors having three direct capacitances such
as shown in Fig. 7, in which the dielectric loss is wholly in the direct capacitances from
the plates to the support, the direct capacitance between the plates including no dielectric
loss. This method, or the use of a variable air capacitor with conductance independent
of setting, is the common method for obtaining standards of zero conductance.
Accuracy. The accuracy of a bridge of this type depends on the accuracy with which
the capacitance standards are known. An overall accuracy of 0.1 to 0.25 per cent for
capacitance is possible for frequencies up to 1 megacycle. The conductance accuracy
stated in terms of power factor is in the order of ±(1 per cent + 0.0001).
DIRECT CAPACITANCE. Direct capacitance may also be measured on the bridge of
Fig. 8 as follows: Ground the point C of the bridge and all conductors of the apparatus
under test except the two terminals between which the direct capacitance is desired.
Connect one of these to C and one to D, and obtain a bridge balance. Then transfer the
terminal connected at C to A, and rebalance the bridge. A little consideration will show
that the only capacitance transferred in this operation is the direct capacitance required,
and the difference between the .balances is therefore equal to
~ twice this capacitance.
A second method which is satisfactory where all the capaci-
tances involved are small, such as the interelectrode capaci-
tances of a vacuum tube, is to connect the capacitance to be
evaluated across CD, all other terminals including ground
being connected to B. The capacitance thus placed across
BC will affect the accuracy of conductance but not of capaci-
tance measurement, and the direct capacitance may be
measured directly,
The modified circuit shown in Fig. 9 has two advantages
for the measurement of direct capacitance. By using a pair
of closely coupled inductors for ratio arms, that is, parallel
windings on a common core, the effect of the capacitance
across BC will be very much reduced. If, in addition, the
capacitance standard is such that capacitance is transferred
from CD to J.D, keeping the total value CA + Cc constant, and a fixed capacitance CD
is connected in series in the D lead, it may be shown that the bridge unbalance correspond-
ing to an unbalance CA — Cc is equal to A — . If CD is made small compared
-
FIG. 9. Bridge for Measure-
ment of Direct Capacitance
T LC T-
Cc + CD, very small values of direct capacitance, as low as 0.0001 j
, may be
with CA
measured.
A third method is by means of the Wagner ground.
The Wagner Ground. A common modification of the simple equal ratio-arm bridge
and of other bridges involves the Wagner ground. This is a simple method of eliminating
the effect of stray admittances, compared with complete shielding of the bridge. Referring
to Fig. 8, but with power source and detector interchanged, it consists of a potentiometer
connected across the input corners AC of the bridge, the adjustable contact being grounded
and adjusted to bring the D corner of the bridge to ground potential. In some bridges,
complex impedances are required instead of resistances for
this balance. It has two disadvantages. First, it requires for
any measurement two balances, namely, the adjustment of
the Wagner ground and of the bridge itself, and these bal-
ances are not independent. This makes the balance pro-
cedure relatively slow and complicated. Second, the quan-
tity measured is the direct capacitance. When the mutual or
grounded capacitance is desired, it must be computed from
the measured values of the individual direct capacitances.
These limitations considerably restrict its usefulness.
THE SCHERING BRIDGE. At high frequencies, adjust-
able resistance standards have serious limitations. Above
about 1 megacycle, the Schering bridge is used to avoid them.
In this bridge a fixed capacitance and a fixed resistance are FlG- 10-
in diagonally opposite arms, and the other arms may be
arranged to allow both capacitance and conductance to be
balanced by variable capacitors. The circuit and balance equations are given in Fig. 10.
K the bridge is balanced and then the unknown is connected across C\ and the bridge
rebalanced by means of Ci and C*, the change in Ci equals the capacitance of the unknown
ftttd tfae change in Cs is inversely proportional to its conductance. If series components
are desired the unknown may be connected either in series or in parallel with Cs- Then Cg
Schering Bridge for
Measurement of Capacitive Im-
pedances
INDUCTANCE AND EFFECTIVE RESISTANCE 11-27
balances for capacitance and Ci for series resistance but the bridge will not be direct reading
for both components.
OTHER METHOBS. Bridge methods have the advantage of a null balance. They do
not have the advantage of both grounded input and grounded output unless transformers
are used. Other methods are available, particularly at high frequencies, which have both
these advantages. They consist essentially of two unbalanced transmission networks
connected in parallel, the required relation between the arms for zero output being that
their transfer constants be equal in magnitude but 180° out of phase (see Section 6).
Commercial measuring circuits of this type are available, known as shunted T and twin/T
circuits.
The most popular method other than null methods is the simple tuned circuit, the con-
dition sought being a maximum or minimum of either voltage or current with variation of
inductance, capacitance, or frequency. A commercial circuit using this method known
as a Q meter is described in article 13.
Practically all these special circuits substitute a capacitance standard for the unknown
in measuring capacitance, the difference between them lying in the method of measuring
the loss. Capacitance is seldom measured in terms of other quantities owing to the
superiority of capacitance standards over all others.
13. MEASTJEEMENT OF INDUCTANCE AND EFFECTIVE RESISTANCE
As for capacitance, the simplest type of measurement is direct comparison, and the
bridge of Fig. 8 is capable of the same accuracy for inductance measurements as for capaci-
tance measurements, limited only by the standards. However, inductance standards are
inherently less satisfactory than capacitance or resistance standards, particularly for wide
inductance and frequency ranges. Accordingly, other less symmetrical bridges are common
in order to take advantage of standards of capacitance and resistance. Of these the
bridges most used are the resonance method with the equal ratio-arm bridge, the Owen
bridge, the Maxwell bridge, and the Schering bridge.
COMPARISON METHOD. This measurement is made by comparing an inductance
in the CD arm with an adjustable standard in the AD arm of an equal ratio-arm bridge
such as shown in Fig. 8. In order to balance the effective resistance component and to
measure it when required, it is necessary to add a series resistance in either the CD arm
or the AD arm, depending on the relative resistance values of the unknown impedance
and of the standard. The usual procedure is to connect a standard resistance by means of a
switch at D to throw the resistance into either arm as required. The bridge permits bal-
anced to ground and grounded measurements, as in capacitance measurements. When
adjustable standard inductances are used, and when the series resistance required is large,
the shielding of the standards becomes cumbersome and the bridge is commonly used
grounded.
The inductance of the unknown is equal to the inductance of the standard at balance.
The effective resistance is given by rx = TL ± rs where rj, is the effective resistance of the
standard inductance and r8 is the setting of the standard resistance, the sign depending on
the position of the switch.
The accuracy of such a circuit depends on the frequency and on the accuracy of calibra-
tion of the inductance standards. An accuracy of about 0.25 per cent for inductance and
2 per cent for resistance is possible for frequencies as high as a megacycle.
Wagner Ground. This can be used with the above method to avoid shielding. However,
the limitations of this method as outlined in article 12 apply equally to inductance measure-
ments.
RESONANCE METHOD. Inductance can be compared with capacitance and fre-
quency either by series or parallel resonance. The series method has the advantage of
giving directly the series resistance and inductance of the coil which are the values usually
desired. It is also inherently a low-impedance circuit, and this is often an advantage
where the voltage available from the power source is limited. The parallel method gives
the equivalent parallel values, which usually require subsequent transformation. It is
inherently a high-impedance circuit.
The principle on which resonance measurements are based is the adjustment of the
capacitor until the tuned circuit has zero or infinite reactance; that is, it is equivalent to a
pure resistance. The measurement is usually made on an equal ratio-arm bridge, but any
bridge that will determine when the impedance of the circuit is a pure resistance and that
will measure the resistance is suitable. The principal objections to the method are that
it is not direct reading and the accuracy is dependent on the frequency of the source.
Series Resonance. For the series measurement by the equal ratio-arm bridge of Fig. 8,
an adjustable resistance is connected in the AD arm and the capacitance in series with the
11-28
ELECTRICAL MEASUREMENTS
unknown in the CD arm. Since the unknown forms only part of the impedance in the CD
arm, balanced-to-ground measurements are impractical and this measurement is usually
made with D grounded. The capacitance is connected from C to the unknown in order
that one terminal of the unknown may be connected to ground. The balance is obtained
by adjusting the standard resistance and capacitance, and at balance the following relation
holds:
oi2LzC4 = 1 or Lx — -^7
orCs
rx is equal to r, less the equivalent series resistance of C8. If the conductance of C, is
used, as it generally is, since when multiple standards are used their conductances add
directly, then
-
* c,
where rx, Lx are the values of the unknown.
ga is the conductance of the standard Ca.
Parallel Resonance. For this measurement the capacitance and the unknown induct-
ance are connected in parallel in the CD arm of the bridge. Either balanced-to-ground
or grounded measurement may be made. Since the resistance required for the balance
may be very high, an arrangement similar to that for a capacitance bridge is customary;
that is, a fixed resistance, usually 10,000 ohms, is connected across CD and the loss is read
as conductance by means of a variable resistance across the AD arm of the bridge. The
balance is then obtained in the same way as for series resonance. Then
_ 1 , ro — TI
where g» is the conductance of the condenser C,,
ro and ri are the open-circuit and final readings of TV
Lp is the parallel inductance of the unknown impedance.
gp is its conductance.
The series equivalents may be obtained by transformation,
Accuracy. The accuracy of resonance bridges depends on the accuracy of both the
capacitance standards and the frequency. Accuracies as high as 0.1 per cent are possible
without extreme precautions. They
are probably the most accurate cir-
cuits for measuring effective resist-
ance, accuracies of the order of 2 per
cent being readily obtainable, even
for high-Q coils.
THE OWEN BRIDGE. This
bridge in common with the Max-
well bridge has the advantage that
inductance is measured in terms
of capacitance and resistance. It
is not frequency sensitive and can
be made direct reading for both
L and r. A shielded circuit for
the Owen bridge is shown in Fig.
11. The equations of this circuit at
balance are
L =
and
FIG. 11. Shielded Owen Bridge for Measurement of In-
ductance and Effective Resistance
proportional to ;
where r2 includes the effective resist-
ance of the unknown. Two methods
of operation are possible. Both C\
and n may be adjustable, and then
the inductance of the unknown is
and the total effective resistance in the CD arm is proportional to 1/Ci.
It is usually more convenient to have Ci fixed or adjustable in a few steps and to have
TZ adjustable. Then by taking a short-circuit reading r0 for r2 it follows that L — Cartf\
and rx = ro — r$. Since the unknown is not connected directly across the arm CZ>, bal-
anced-to-ground measurements are impractical. Since the resistances are capable of
adjustment to their nominal values with a high degree of precision, the bridge is direct
reading for both inductance and resistance without the need for calibration. Also, the
INDUCTANCE AND EFFECTIVE RESISTANCE 11-29
range of inductance may be made very wide since n may be designed to have as many as
six or seven dials. The bridge is not so statable for the measurement of effective resistance
on account of residual reactances in the various bridge arms and difficulties in shielding
always encountered in arms having series impedances.
The shielding is made only partially complete in the interest of simplicity. The resist-
ance TCD is used to compensate the shield capacitance across JJ>, a resistance being
required because of the 90° phase relation of the ratio arms. With this circuit inductance
accuracies as high as 0.1 per cent are usual at audio frequencies. It is not as satisfactory
at higher frequencies as the following bridges.
THE MAXWELL BRIDGE. In this bridge fixed resistors are used in diagonally oppo-
site arms. The inductance and effective series resistance of the unknown are then balanced
by capacitance and conductance respectively in the standard arm. The circuit and balance
equations are shown in Fig. 12. If ra and r& are not pure
resistances, the balance equations still hold if their phase
angles are equal but of opposite sign. If gs is designed to read
directly in conductance (see article 8) the bridge may be made
direct reading for both L and r. This feature makes the
bridge as attractive as the Owen bridge. In addition, since
it has no series connections in the arms, stray admittances
may be compensated more readily and the bridge is satis-
factory at higher frequencies.
THE SCHERING BRIDGE. This is described in
article 12. It is essentially a capacitance bridge but
will measure inductance as a negative capacitance and
is particularly adapted to high-frequency measurements f10- 12- Marwell Bridge for-
of low-Q impedances which may have either positive or M<Sd^th?aSrtSSM"
negative reactance.
METERING. The values of inductance and resistance of magnetic-core coils are usually
a function of the saturation. It is therefore desirable to know the current through, or the
voltage across, the coil when measured. In any so-called ratio-arm bridge, where two
adjacent arms are invariable, the current through the unknown, or the voltage across it,
will have a definite relation to the total bridge current or voltage, determined only by the
ratio arms and the choice of input and output corners. Thus in Fig. 8, which uses a
current connection, the current input divides at balance in proportion to the admittances
of the ratio arms, and a meter in the input circuit can be calibrated to read directly the
current through the unknown. In Fig. 11, which shows a voltage connection, tbe input
voltage divides at balance in proportion to the impedances of Ca and r&, and a meter across
the input can be calibrated to read directly the voltage across the unknown. Here the
calibration will be a function of frequency but is independent of the value of the unknown.
Bridges of the so-called product-arm type, having the fixed impedances diagonally
opposite, such as the Maxwell and the Schering bridges, do not have this feature, and the
metering is usually done by connecting a vacuum-tube voltmeter directly across the un-
known.
SUPERIMPOSED MEASUREMENTS. Measurement of inductance is sometimes
required for magnetic-core coils, with direct current flowing through the winding. Such
measurements may be made on an equal ratio-arm bridge such as that of Fig. S, applying
the direct current across the BD corners and separating the direct current from the alter-
nating current where necessary by stopping condensers and a choke coil. A more con-
venient bridge is the Owen bridge of Fig. 11. If direct current is applied across BD and
alternating current across AC, the only additional apparatus required is a stopping con-
denser in the detector circuit. The Maxwell bridge is also well adapted to making these
measurements.
OTHER METHODS. At very high frequencies where extreme circuit simplicity Is
desirable, the simple tuned circuit is commonly used. The method of measurement is as
follows.
If a voltage is applied to an inductance in series with a capacitance as shown in Fig. 13
and either L, C, or co is varied to give maximum voltage across C, then
oji = —
coC
and
Ez <*>L 1
Ei ~~ r
where E\ is the voltage across the tuned circuit.
&i is the voltage across L or C.
r is total resistance of the circuit.
11-30 ELECTEICAL MEASUREMENTS
Thus, if the values of EI, E*, and w are measured, the inductance and resistance of a
coil can be determined if the capacitance and resistance of the capacitor are known, and
vice versa. A refinement of this circuit consists of adjusting the input voltage to a definite
value either directly by a voltmeter or by adjusting the current into the known resistance
rc. Then the voltmeter across G may be calibrated in terms of Q. If the capacitor C
has negligible loss, this will be the Q of the coil. Commercial measuring sets called Q-
meters are available with self-contained oscillator, low-loss variable-capacitance standard,
and vacuum-tube voltmeter, which are direct reading for Q. They are satisfactory up
to 200 megacycles or higher.
There are a number of errors in the Q reading that may be corrected for when known.
The resistance r of the circuit includes the equivalent series resistance of the capacitor,
which includes its dielectric loss and the admit-
tance of F2- The frequency response of the
voltmeters may not be flat. If the input
current is controlled, EI is affected by change
in impedance of rc due to reactance or skin
effect, and by the shunting effect of r. These
errors vary independently with Q, X, and &> so
much that no average figure for accuracy
applies. For values of Q about 100, and values
FIG. 13. Q Meter Circuit of X about 100 ohms, accuracies of 5 per cent
can be expected up to 25 megacycles.
MUTUAL INDUCTANCE. Mutual inductance between two coils can be determined by
measuring the self-inductance of the two windings by any suitable method, with the wind-
ings connected first series aiding and then series opposing. The difference between the
two values is four times the mutual inductance. The ground conditions are usually dif-
ferent for the two measurements from the actual operating conditions. This may be a
source of error, particularly where the coupling is low. The ratio of secondary voltage to
primary current may be determined directly by thermocouple and vacuum-tube voltmeter.
14. SIGNAL GENERATORS AND DETECTORS
The following discussion is limited to the special requirements which apply to use with
measuring circuits such as those described. More complete information may be found
in articles 36 to 40.
SIGNAL GENERATORS. Many single-frequency generators are available in the
audio-frequency range provided the requirements are not severe. However, the tuning
fork operated by a microphone or vacuum tube, and the rotating generator, represent
practically the only types, other than vacuum-tube oscillators, with satisfactory charac-
teristics for precise work. Where a range of frequencies is necessary and particularly for
frequencies above the audio range, vacuum-tube oscillators are used almost exclusively.
VACUUM-TUBE OSCILLATORS. The principal requirements for an oscillator for
measurement purposes are adequate output level, low level of harmonics and other spurious
frequencies, and high stability of frequency and output level with respect to time and
temperature. The emphasis on these requirements depends on the type of measurement.
The output level should be high enough to insure that the input level to the detector is
above thermal noise for the most precise balance. An output of 0.1 watt is usually ade-
quate. Level stability requirements are more lenient for null measurements. Harmonic
requirements are more lenient for null measurements which are not frequency dependent.
In general, when untuned detectors are used, harmonics should be held below 3 per cent
of the fundamental, and for null resonant measurements, below 1 per cent. Harmonics
may be suppressed by filtering external to the oscillator, either before or after the measuring
circuit. The former is preferable in so far as it prevents production of false signal by modu-
lation in the measuring circuit, but it places severe modulation requirements on the filter.
Oscillators are in general of three types, according to the type of frequency-selecting
network used, namely, crystal, LC, and rC oscillators. The crystal oscillator is the most
stable and is the preferred type for fixed frequency applications over the frequency range
for which crystals are applicable, about 10 kc to 10 me. The LC oscillator is the most
versatile and can be used over the whole frequency range up to the maximum frequency
at which lumped constants are practical. At low frequencies, the necessity of using coils
of large physical size to obtain a high Q makes it cumbersome, and the rC oscillator is
preferred. This oscillator has the advantages that the components are small even at very
low frequencies, and it may be made direct reading more readily. It is suitable for fre-
qT*eiicies lower than 1 cycle up to about 100 kc, where, in spite of lower stability, it com-
petes mta tiie LC oscillator because of the direct-reading feature.
BIBLIOGRAPHY 11-31
HETERODYNE OSCILLATORS. These oscillators, having an output frequency
which is the difference between the frequencies of a fixed and a variable oscillator, can be
made to cover a wide frequency range with a single continuous control. This has two
advantages: it allows them to be made direct reading over wider ranges than the conven-
tional LC oscillator, and the broad continuous range makes them suitable for sweep
frequency measurements required in recording, and in cathode-ray visual indication, of
frequency characteristics.
DETECTORS. Detectors, as distinct from actual measuring instruments, are limited
to the detection of null balances and equality of output from different circuits or from
different arrangements of the same circuit.
The principal requirements are adequate sensitivity for the accuracy required, sufficient
discrimination against harmonics, and stability of gain with time and temperature.
Sensitivity can usually be obtained by amplification. The limit is determined by thermal
noise, which depends on the band width. This limit is approximately 10~20 watt per cycle
band width. For instance, using a detector with a 1000-cycle band width working out of a
bridge of 1000 ohms impedance, minimum signal to exceed thermal noise will be 10 ~17
watt or 0.1 }j.voli.
The harmonic suppression required depends on the oscillator harmonics, the method of
measurement, and the characteristics of the unknown. Gain stability requirements are
least severe for null measurements. They are most severe in adjusting two outputs to
equality using some form of suppression.
The telephone receiver with or without preceding amplification is the simplest and most
sensitive detector within the audio-frequency range. Owing to the frequency charac-
teristic of the ear and of the receiver, considerable discrimination against harmonics can
be obtained in the frequency range where they are most sensitive. At higher frequencies,
the heterodyne type of detector giving an audio output may be used with the receiver.
It has the advantage of giving considerable discrimination. In all detectors care must be
taken that the harmonics do not overload the input sufficiently to cause a. false signal due
to modulation.
In addition to the telephone receiver, a rectifier, such as copper oxide or a vacuum tube,
may be used with a d-c instrument or cathode-ray-tufoe indicator. These require greater
amplification and more discrimination.
BIBLIOGRAPHY
Campbell, A., and Childs, E. C-, The Measurement of Inductance, Capacitance, and Frequency, Macmil-
lan & Co., London, 1935.
Edgecumbe, K. W. E., and Ockenden, F. E. J., Industrial Electrical Measuring Instruments, Pitman,
London, 1933.
Terman, F. E., Radio Engineers Handbook, McGraw-Hill, New York, 1943.
Chaffee, E. L., Theory of Thermionic Vacuum Tubes, McGraw-Hill, New York, 1933.
Moullin, E. B., Radio Frequency Measurements, Griffin, London, 1926.
Hund, A., High Frequency Measurements, McGraw-Hill, New York, 1933.
Hague, B.T Alternating Current Bridge Methods, Pitman, London, 1923.
Glazebrook, Sir R., Dictionary of Applied Physics, Macmillan & Co., London, 1923.
Hartshorae, L., Radio Frequency Measurements by Bridge and Resonance Methods, Chapman and Hall,
London, 1941.
Henney, K., The Radio Engineering Handbook, McGraw-Hill, New York, 1941.
Rider, Jr., Vacuum Tube Voltmeters, J. F. Rider, New York, 1941.
Bur. Standards Circ. 74, Radio Instruments and Measurements.
Grondahl, L. O., The Copper-cuprous-oside Rectifier and Photoelectric Cell, Rev. Modern Physics, VoL
5T 141 (1923), including extensive bibliography on copper oxide rectifiers.
Aiken, C. B., Theory of Diode Voltmeters, Proc. I.R.E., Vol. 26, 859 (1938).
Miller, J. H., Thermocouple Ammeters for Ultra High Frequencies, Proc. I.R.E., Vol. 24, 1567 (1936).
Behr, L., and Tarpley, R. E., Design of Resistors for High Frequency Measurements, Proc. I.RJE.,
Vol. 20, 1101 (1932).
Campbell, G. A., The Shielded Balance, Elec. World, Vol. 43, 647 (1904).
Ferguson, J. G., Shielding in High Frequency Measurements, Trans. A.I.E.E., Vol. 48, 1286 (192§>.
Campbell, G. A., Measurement of Direct Capacities, Bell Sys. Tech. J"., Vol. 1, 18 (1922).
Christopher, A. J., and Kater. J. A., Mica Capacitors for Carrier Telephone Systems, Trans. AJ.E.E^
Vol. 65,670 (1946).
Cone, D. I., Bridge Methods for Alternating Current Measurements, Trans. A.I,E.E.t Vol. 39, 1743
(1920).
Behr, L., and Williams, A. J., The Campbell-Shackelton Shielded Ratio Box, Proc. I.R.E., Vol. 20,
969 (1932).
Wagner, K. W., Zur Messung dielektrischer Verluste mit der Wechsektrombrucke, Elekt. Zeits.,
32 Jahrgang, pp. 1001-1002.
Kupfmuller, Von K-, tlber eiae techmsche Hochfrequenz Messbmcke, Elek. Mack. Tech., 1925, p. 263.
Ferguson, J. G., Classification of Bridge Methods, Trans. A.I.E.E., VoL 52, 861 (1934).
Wilhelm, H. T., Impedance Bridge with a Billion to One Range, BeU Td. Rec.r March 1945.
Caial&gs of the Leeds and Noorthrup Co., General Radio Co., Westinghouse Corp., aad Weaton Electrical
Instrument Co,
General Radio Experimenter*
Definitions of the A.S.A.
11-32
ELECTRICAL MEASUREMENTS
WIRE LINE MEASUREMENT
By H. J. Fisher
Attenuator
FIG. 1. Comparison Method for Measuring Insertion Loss
15. TRANSMISSION MEASUREMENTS
Transmission measurements evaluate a circuit or facility (wire line, cable, radio circuit,
three- or four-terminal network, etc.) in regard to its ability to transmit telegraph, voice^
modulated carrier, television, or other communication signals. This evaluation usually
involves two criteria, (1) effect on signal amplitude and (2) effect on signal shape. It has
been found convenient to
express the criteria in
terms of steady-state mea-
surements of loss or gain,
phase shift, and envelope
delay distortion vs. fre-
quency, and, in addition,
non-linear distortion
(compression, expansion,
interehannel modulation
cross-talk) as a function of
signal amplitude. Usu-
ally the device or circuit
to be measured is one of many connected in tandem between the original signal source
and the final receiver, and it is desired to know the effect on overall transmission caused
by inserting the portion in question. Since the individual portions of a system are usually
designed to have a nominally constant impedance (vs. frequency) of a standardized value
(e.g., 600 «, 135 co, 75 w) the insertion transmission can be measured directly with test
equipment having the
same nominal impedance.
Impedance variations
with frequency of the unit
to be measured, of the
connected circuits, or of
the testing equipment,
will produce errors in the
insertion transmission
measurement which must
be considered. If all im-
pedances are designed to
have less than 5 per cent
reflection coefficient these
Avc maintains constant voltage wh.ic.tL fs
equivalent to zero impedance generator
errors usually can be ne-
glected.
INSERTION LOSS OR GAIN.
o
ra
t System or um
t to be measured
|
r<
5i>i z
^*"^*2
~1>
S~
N
D-bin
mfiter
1
y »"*"
I
1
f
V
^
H Avc
r~ "
Ifc
* *
vlW (0-dbm)
reference
standard
^n
IMW (0-dbm)
reference
standard
Ibrating
needed
Sending end calibrating
circuit used as needed
1 IMW (Q-dbrn)|
[sending source)
Receiving end caf
circuit used as
FIG. 2A. Straightaway Method for Measuring Insertion Gain or Loss
Comparison Method. Figure 1 shows a commonly
used setup for measuring insertion loss. The attenuator is adjusted until equal readings
are obtained on the meter for the two positions of the key. When measuring gain the
attenuator is connected in tandem with the unknown. Systems or units having input
frequencies that differ from the output frequencies such as modulators or mixers can be
measured with this setup provided that the
detector and attenuator characteristics do not
change over the frequency range of interest.
Straightaway Method. Figure 2A shows a
setup for making this type of measurement.
A circuit of this type is required when the in-
put and output terminals are not available at
the same location. The circuit is self-explan-
atory except for the following items.
Dbm Meter. This is usuallv a broad-band
FIG. 2B.
Rectifiers
DBM Meter
amplifier having adjustable gain in 10-db steps followed by a linear rectifier (diode or
varistor) with a meter calibrated in dbm over about a 13-db range. See Fig. 2JB.
1 Milliwatt (0 Dbm} Reference Standard. This is usually a thermocouple circuit of the
correct impedance arranged to be calibrated by standard d-c power as determined by a d-c
milliammeter.
TRANSMISSION MEASUREMENTS
11-33
Voltage Method. For making measurements on working systems without causing dis-
turbance to the working signals, a frequency selective voltmeter is used (see reference 3),
This is a high-impedance selective heterodyne detector of adjustable sensitivity in, say,
10-db steps followed by a linear detector and dbm meter. The measurements are usually
made at the pilot frequencies or other frequencies not in the signal channels. Since the
working signals may be at higher levels than the pilots, it is important that thej&rst
modulator and input amplifier be operated at levels low enough to reduce the error due to
inter modulation products falling at the measuring frequency. Frequency discrimination,
at intermediate and final frequency stages, sufficient to eliminate all other unwanted
frequencies is obtained by means of quartz crystal filters and selective interstage circuits.
The required discrimination can be reduced by about 26 db by the use of a linear rectifier
rather than a peak detector and about 23 db with square-law or thermal-type indicators.
MEASUREMENT OF INSERTION TRANSMISSION (LOSS OR GAIN) OF CIR-
CUITS AND UNITS HAVING MISMATCHED IMPEDANCES. As stated above,
when the reflection coefficient of the circuit or unit being measured and the test equipment
are less than 5 per cent when re-
rJH
Line amplifiers
453 kc (A)
-57 kc (B)
lOOO'v
loob'v
FIG. 3 A. Modulation Measurements on
Telephone System
ferred to the nominal impedance
the measured insertion transmis-
sion is usually negligibly different
from the true insertion transmis-
sion. In some broad-band systems
the impedances of the tandem,
components vary considerably
with frequency from the nominal,
and the reflection losses incurred
are sometimes employed in overall
equalization of the system. When
measuring components of such a
system with nominal impedance
test equipment there is a discrep-
ancy between the measured and
actual insertion transmission. When
measuring with a voltmeter type
of circuit the discrepancy is differ-
ent and usually larger. This in itself causes no great complication in the maintenance
of these systems since the operating limits are specified having in mind the type of test
equipment which is used. Difficulty does arise when attempts are made to correlate
measurements made by the two methods. A calculation using complete impedance in-
formation and rigorous insertion transmission equations is necessary.
INTERMODTJLATION DISTORTION MEASUREMENT. As a result of non-linear
distortion (such as occurs in vacuum-tube amplifiers) in a transmission system, frequen-
cies other than those applied to the
I Line section j — *49 kc (2 A-B)
10QO<v
DBM meter
Overall Carrier
-»-49 kc (2 A-B)
-*~53 kc (A)
-»-57 kc <B)
including .
amplifiers j ~ **53 kc (A)
Sectionalizing filter
suppresses 49 kc
7
input of the system are produced. For
example, if two tones are applied to
the system, say (a) and (6), new com-
ponents having frequencies such as 2a,
26, a =t 6, 2a ± 6, 26 ± a, 3a, 36., etc.
are produced. In some cases, these
new frequencies fall outside the band
of interest and need not be considered,
but in wide-band systems many of
these products fall within the trans-
mitted band. In multichannel sys-
tems these new frequencies may result
in interchannel interference. To pre-
vent this interference from exceeding
allowable amounts, measurement of intermodulation distortion is a necessary part of the
maintenance of multichannel systems.
There are two types of test: (1) an over-all test to check whether the circuit as a whole
meets specified requirements; (2) a test on a portion of the circuit or on individual re-
peaters to locate the defective tubes or other component or a maladjustment.
Figure 3A shows how the over-all test is made on a typical 12-channel carrier system.
Channels 1 to 9 are continued in operation, channels 10, 11, and 12 being turned down.
Channels 11 and 12 are energized with 1000-cycle power of specified level, and after pass-
log through the terminal modulating equipment they appear on the line as 53 and 57 kc.
Selective detector
including DBM meter
Preselection 'filter
passes 49 kc
PIG. 3B. Modulation Measurements on Line Section
11-34
ELECTRICAL MEASUREMENTS
As a result of third-order intermodulation in succeeding amplifiers, 49 kc (2a — o) is pro-
duced. At the receiving end this product appears in voice channel 10 as 1000 cycles,
where it is measured with a sensitive dbm meter. The 2a — b product is used for this test
because it is the product most likely to be excessive. The reason for this is that the modu-
lation component produced at each repeater tends to add in phase with the components
produced by other repeaters whereas most other products add on a random basis.
To localize sources of excessive intermodulation the line may be sectionalized as shown
in Fig. 3B. In this case, the three channels are turned down as before, the 53 and 57 kc
originating as 1000 cycles at the transmitting terminal. Any 49 kc produced between the
terminal and the suppression filter is suppressed and the test is essentially originated at
that point. The selective detector and preselection filter are portable and can be moved
as near to the suppression filter as desired, for example close enough to include only
one repeater-
In other multichannel systems the modulating test tones are applied directly to working
lines by means of high-frequency oscillators. They are allocated in spaces between work-
ing channels and are also chosen so that the product being measured, which may be
2a, 3a, 2a — 6, etc., also falls in an idle part of the spectrum.
See references 1 to 3.
INSERTION PHASE MEASUREMENT. This measurement is almost entirely re-
stricted to the laboratory, where it is particularly useful in connection with the measure-
ment of the feedback factor (/*$) loop of a feedback amplifier (see references 4 and 5) and
Circuit >impedance BO-/ Differentia!
ndertestl ( probe ' 7 v < voltmeter
Rectifie
Differentia! meter
response=
K (rectified sum-
rectiiied difference).
FIG. 4J.. Direct-reading Phase-measuring Circuit
the insertion- phase of networks (see reference 6). In connection with transmission of
television signals over coaxial cables phase data are obtained indirectly by the integration
of the envelope delay characteristic.
Figure 4J. shows a direct-indicating type of circuit by means of which the ju$ character-
istic can be quickly obtained. Attenuators A and B are adjusted so that the input and
output vectors are equal in magnitude. The loss or gain of the circuit under test can be
obtained from these attenuator readings. By an alternative arrangement, using avc
amplifiers this can be accomplished automatically. Assuming that vectors of equal mag-
nitude are applied to the hybrid coil the meter reading will indicate the phase difference
directly. Figure 4B shows the characteristics of the direct-indicating phase indicator.
The difference of the rectified sum and difference outputs is used because it permits the
r/7T CX ~
response = kf cos ( - -f- -
By
tltis mean® a quite linear indication of phase difference can be obtained over a ISO0 range
and wiikin the range of 90° ± 45° the deviation is usually negligible. This range of good
TRANSMISSION MEASUREMENTS
11-35
-H.O
0 40 80 120 ISO
dboz=angJe between vectors, degrees
FIG. 4B. D-c Response vs. Differ-
ence in Phase of Two Equal-frequency
Sine Waves
linearity may be shifted to any other desired portion of the range by means of a calibrated
phase shifter in one of the branches. In Fig. 4A a
modulation method is shown to provide selectivity to
reduce the effect of noise and to permit the use of
fixed-frequency circuits, but successful broad-band sets
have also been constructed. This type of set is also
easily adapted to the automatic recording of ju£.
Other types of phase-measuring circuits have been
devised. Generally they require the adjustment of the
reference and unknown vectors to equal magnitude.
Phase may then be computed from the difference in
magnitude of their sum and difference, or, by means of
an adjustable calibrated phase shifter (of any of several
well-known types) placed in either branch, the sum or
difference may be adjusted to a null and then the phase
shift may be read directly from the calibrated phase
shifter, due allowance being made for quadrant deter-
mination. In a variation of this method suggested by
S. T. Meyers and used extensively, the sum or difference
is adjusted by means of a calibrated phase shifter
to equality with the reference and unknown vector. This indicates a 120° phase difference
between the two applied vectors which when added to or subtracted from the indicated
phase shift depending on the
quadrant gives the actual
phase difference.
Another widely used phase-
measuring circuit is described
in W. P. Mason's patent U. S.
1,684,403. This is known as
the sum-and-d'iff erence
method and requires only
commonly available equip-
ment such as an oscillator, a
detector, and attenuators (see
reference 6).
INSERTION ENVELOPE
DELAY DISTORTION
MEASUREMENT. In some
types of communication, such
as television, telephoto, and
telegraph, distortion of signal
shape is more important than
for ordinary telephone com-
Ehvebpe tkJay distortion
indicating meter
LuoearN
amp. reck
Fia. 5. Envelope Delay Distortion Measuring Circuit
munication (see references 7—12). Equally as important as attenuation distortion (vs.
frequency) as a criterion for distortion of signal shape is envelope delay distortion. Enve-
lope delay is expressed as dfi/du, and in an
ideal system it is independent of frequency
in the range of interest. Envelope delay dis-
tortion is corrected by means of phase-shift
networks, the objective being to obtain a
phase shift vs. frequency characteristic in the
frequency range of interest having a slope
dfi/d<u which is constant. For networks and
amplifiers the necessary phase data are usu-
ally obtained directly from phase measure-
ment. For long lines it is difficult to make
accurate straightaway phase measurements
on account of the instability of the loss and
phase of the line which may include many
repeaters, and the usual practice is to measure
envelope delay distortion. From these data
the phase requirements for the equalizer can
be computed.
Envelope delay
distortion, ~~
jft\rTQ<zf*rnritfo
irf
FIG. 6.
Typical Phase Characteristic of a Trans-
mission Line
Figure 5 shows a circuit for making straightaway measurements of the envelope delay
distortion of long coaxial circuits. At the sending end four frequencies of equal amplitude
11-36 ELECTRICAL MEASTJBEMENTS
are transmitted: /i + p/2 and fi — p/2, representing the reference signal; and /2 + p/%
and fz — p/2, representing the test signal. Referring to Fig. 6, assume that the line under
test has a phase vs. frequency characteristic as shown. At the distant end of the line each
of the four frequencies will have been shifted in phase by different amounts j3(i_p/j),
£d + p/s>» ftt-p/2), and 0(1+ p/2). Now we can say that
Aft = £(I+p/2) - |8(l_p/2), A02 = /3(2-f-j>/2) — /3(2_p/2>
and if p is chosen small enough then for all practical purposes
Aft dft A& __ d&
_, — = __ — and r — T
2?rp ao> 27rp oco
The envelope delay distortion f-p - — * J is equal to - g6Q microseconds.
If /2 is varied over the band of interest the measurement of A& — Aft will represent
envelope delay distortion referred to the envelope delay at the reference frequency /i. If
the set is given a "zero" adjustment by means of the "zero adjust" phase shifter so that
with a distortionless line or resistance pad in place of the line under test the indicated
envelope delay distortion is zero then the equipment at the receiving end will provide an
indication proportional to (Aft — Aft) and therefore also to I — ) , the envelope
\O6) aw /
delay distortion. The receiving circuit functions as follows: the reference signal and the
test signal are separated by filters as shown and then demodulated to obtain the difference
products. The outputs of the two demodulators are of the same frequency p but have a
phase difference equal to Aft — Aftt assuming that the zero adjustment has been made.
The amplitudes of the two vectors are made equal by means of the attenuators (which
incidentally provides a measure of attenuation distortion) and combined in the hybrid
coil from which two new vectors are obtained, one whose amplitude is a function of the
sum of the two vectors (^Afe + l?4/Ji) and the other whose amplitude is a function of the
difference (EAfo — EA&I) . These new vectors are rectified separately in linear amplifier
rectifiers, and the difference of the d-c outputs is indicated on the two-winding zero
center meter. By the use of the difference of the sum and difference d-c outputs the indi-
cation obtained is very closely proportional to Aft — Aft from 0 to ±180° and, as shown
above, is therefore also proportional to ( -r-^ IT I » *ke envelope delay distortion in
\oto uco/
microseconds. If the area under the plotted curve is integrated step by step by means
of a planimeter or graphical methods, the phase vs. frequency characteristic can also be
obtained which is the form of data required for use in designing phase-correcting networks.
By the introduction of a motor-driven signal generator and interlocking arrangements
at the sending end and avc amplifiers in place of the attenuators and a recording meter
at the receiving end, this circuit can be adapted to automatic recording of both the attenu-
ation and envelope delay distortion vs. frequency characteristics.
After the initial phase correction is made by means of phase correctors in the line, the
residual delay distortion is considerably reduced and it is necessary to increase the delay
sensitivity of the measuring circuit to obtain data for more accurate phase equalization;
this is accomplished by insertion of harmonic multipliers at A. Similarly the phase sensi-
tivity may also be increased by increasing the frequency interval, 33. The objection to
this is that it does not catch the narrow interval variations.
16. NOISE MEASUREMENTS
Telephone circuit currents other than those produced by acoustic pressures on the
transmitters (e.g., currents produced by electromagnetic or electrostatic induction from
power circuits or from other telephone circuits, currents produced by thermal noise,
vacuum-tube noise, defective components, etc.) produce noise in a telephone receiver
connected to the circuit, these currents being called noise currents. Not all frequency
components of noise have the same interfering effect on a telephone conversation, since
the human ear and the telephone system do not respond equally to all frequencies. ' (See
also Coordination of Communication and Power Systems, Section 10.) A measurement of
the total noise power on a telephone circuit would, therefore, not be a true indication of
its interfering effect.
For many years noise currents were measured by comparing the actual noise as heard
in a receiver to an adjustable standard noise produced by a buzzer, the ear weighting the
different frequency components of the noise. Difficulty in comparing the noise with the
CROSS-TALK MEASUREMENT
11-37
standard when it did not have the same frequency components, and variations between
different observers when measuring the same noise, resulted in the development of meter
methods, thejdevice for measuring telephone circuit noise being known as a circuit noise
meter or noise-measuring set (see references 13 and 14). This consists of a high-gain
amplifier a weighting-network, a rectifier, and a d-c meter as shown in Fig. 7.
600o>
FIG. 7. Circuit Noise Meter
A typical weighting network and amplifier together have the response characteristic as
shown in Fig. 8. This curve is based on a large amount of experimental data and takes
into account the typical receiver-ear sensitivity and terminal trunk transmission character-
istics. For lines carrying program, the weighting characteristic would be different, giving
more weight to the upper and lower frequencies.
The rectifier circuit has been designed so that the d-c output for a steady-state complex
input to the rectifier is proportional to the square root of the sum of the squares of the
individual single-frequency voltages in the complex input. The output is a function of
the average power impressed on the rectifier and
not of wave shape.
A limited db scale on the meter and a gain con-
trol calibrated in decibels are provided for indi-
cating the noise level in decibels above "reference
noise," which is the term given to any circuit noise
which would produce a meter reading of zero, the
same reading as would be produced by sending
10~12 watt of 1000-cycle power into the circuit
noise meter (600 ohm input) .
Reference noise is defined in this manner so as
to facilitate calibration and measurement. For a
single type of telephone instrument and corre-
sponding weighting network the definition is suffi-
cient. However, there are several instruments
with different frequency-response characteristics,
and each requires a separate weighting network.
The method of calibration makes these networks
all give the same reading for a 1000-cycle input,
but noise measured as equal with different net-
works may not be equal in interfering effect when
heard with the corresponding instruments. In
practice, it is customary to express noise magni-
tudes in dba (decibels adjusted) by adjusting the
reading in db above reference noise so that equal magnitudes (in dba) represent equal
interfering effects for different types of instruments. A different adjustment is required
for each type of telephone instrument.
The meter and associated circuits have a dynamic characteristic such that the response
to sounds of short duration approximately simulates that of the ear.
/
"""s
^
10
/
^
x
o
\
X
1->o
s
\
£
v
S,
° 30
\
<D 40
•3
=§ 5Q
60
0 1 2 3 4 E
Frequency-kilocycles per sec
FIG. 8. Frequency Characteristic o
Typical Weighting Network
17. CROSS-TALK MEASUREMENT
Transmission between separate communication circuits is called cross-talk* When the
cross-talk comes principally from one other circuit, it is measured in the same way as a
transmission loss by sending testing power into the disturbing circuit and measuring the
cross-talk power received in the other, the ratio between the powers being expressed in
decibels, since, if a circuit is not overloaded, the ratio is substantially independent of the
actual power. This type of measurement is, called a cross-talk coupling measurement.
In measuring the cross-talk coupling between two coterminous two-wire circuits, the
generator which supplies the testing power and the receiving device which measures the
received power are connected at the same ends of the circuit as in Fig. 9, the measurement
being called a near-end measurement. Four-wire and carrier circuits have separate
transmitting and receiving paths. For these types of circuits, it is, therefore, often desir-
11-38
ELECTRICAL MEASUREMENTS
able to connect the disturbing generator and the receiving device at opposite ends of the
circuits, as shown in Fig. 10, this type of cross-talk coupling measurement being called a
far-end measurement.
Disturbing Circuit
Disturbed Circuit
FIG. 9. Near-end Cross-talk Coupling Measurement
Disturbing Circuit
Disturbed Circuit
FIG. 10. Far-end Cross-talk Coupling Measurement
As the frequency of the disturbing power is changed, the cross-talk coupling between
two circuits varies over a wide range. Single-frequency cross-talk measurements are
therefore of little value, and generators of complex wave shape are used to obtain results
approximating actual talking conditions. Either warbler oscillators or tube noise genera-
tors whose energy-frequency spectra are shaped to simulate the human voice are used as
power sources. The warbler oscillator contains a frequency-changing device that causes
the frequency to sweep over a wide range several times per second. The meter in the
receiving or measuring device averages the results over the range.
Except when there is trouble, the cross-talk between any two circuits is generally very
small. However, when there are many circuits in a group, as in telephone cables, each
may produce a small amount of cross-talk in any one circuit so that the total cross-talk
in that circuit may be noticeable. Coming from so many sources, it is usually unintel-
ligible and is commonly known as "babble." The amount of babble varies with the
actual volume of speech on the other circuits, being greatest at periods when the greatest
number of circuits are in use.
Since the sources of babble are numerous* and since the volume on the disturbing circuits
cannot be controlled, the babble noise on a circuit must be measured in some such
manner as speech volume, or noise, the measurement being one of power, rather than a
power ratio measurement as in cross-talk coupling.
Tests are made by connecting a high-impedance vacuum-tube measuring device across
an idle circuit. This receiving device is similar to that used in transmission level or volume
tests with the exception that the amplifier does not have a uniform frequency response, the
Pu!se characteristic of the amplifier being simi-
generator lar to that used in noise measurements.
j 1 -A- ^ If observations with this device for short
' — i — ' periods during several successive days
show no abnormal conditions, the circuit
is considered satisfactory. A high-imped-
ance device is employed so that it will
not interfere with normal use of the circuit.
Tertntnation
Transmitted
| - pulse
I Reference line
18. ECHO TESTING OF LINES
Reflections
from
Irregularities
This method of test is an adaptation of
radar methods and has been used in two
principal applications: (1) location of
gross faults in cable and open-wire cir-
cuits, and (2) detection of irregularities of
coaxial cable circuits used for television.
Figure 11 shows a circuit applicable to this test. The fundamental circuit is similar for
both applications, the differences being in the shape and length of the transmitted pulses,
t&e reputation rates, and the sweep speeds (see references 12, 15, and 16).
Echo Indicator
11-40 ELECTRICAL MEASUREMENTS
resistance and reactance curves are no longer smooth but change periodically, curve B
showing the effect of an irregularity on the effective resistance. The reactance changes
in a similar manner. This effect is utilized in locating the irregularity, as there is a relation
between the separation of peaks on the curve and the distance to the irregularity.
When an alternating current strikes a circuit irregularity such as a sudden change in
impedance, some of the current is reflected towards the sending end, the amount so re-
flected depending upon the size of the irregularity. Sometimes this reflected current aids
the current entering the line and sometimes it reduces it, depending upon the distance to
the irregularity and the frequency. When the distance from the sending end of the line
to the irregularity is great a larger number of wavelengths is included between the two
points than when the line is short; consequently a smaller change in frequency is necessary
to add an extra wavelength. Each wavelength, half of which adds to and half of which
subtracts from the original current, thereby decreasing or increasing, respectively, the
impedance of the circuit, causes a peak or hump in the curve.
As an example of the manner in which the distance to an irregularity can be deter-
mined (see Fig. 12), let d be the distance to an irregularity. The reflected current must
travel from the sending end to the irregularity and back again to the starting point, so
that it really travels twice the distance or 2d. If the length of one wave is TFi, the total
number of wavelengths in the reflected current equals twice the distance divided by the
wavelength. Let the number of waves be designated by N; then N = 2d/Wi at some
particular frequency which can be called fa. Assume that fa is the frequency corresponding
to one of the peaks on the impedance curve.
As brought out in the foregoing, when the frequency has been increased so that one
more wavelength is included in the double length of line, another peak will be produced
in the impedance curve. Let this frequency be designated as /2. There are now N -f 1
wavelengths at a frequency fa, or N + 1 = 2d/W$. The distance d to the irregularity has
not changed, but the length of one wave has changed to some value W%.
As the wave travels along a telephone line at practically the same velocity at all fre-
quencies, the wavelength can be expressed in terms of velocity and frequency. If an alter-
nating current flows over a circuit at some velocity V miles per second, the length in miles
of any one wave, W, is equal to the velocity divided by the number of waves per second,
or the frequency. In other words, W — V/f.
As shown above, the number of waves in the double path of the reflected current is
equal to N for frequency fa and N -f- 1 for frequency h- In turn N — 2d/Wi and N -f 1
= 2d/W*. Since the wavelength equals the velocity in miles divided by the frequency,
the wavelength for any particular frequency such as / equals the velocity divided by
that frequency. Therefore,
and
Substituting these values of W\ and Ws in the equations
N = —
and
2d_
respectively. Then
2J/F 24A
/i ~ F
and
The frequency fi represents one peak on the curve, and /a represents the next peak as the
frequency increases. From the curve can be determined the number of cycles difference
in the two frequencies representing adjacent peaks, this difference, of course, being equal
to A — fa. Combining the two equations above so that the term /2 — fa will be present,
subtract N from N •}- I, Then
D-C AND LOW-FREQUENCY LINE TESTING
11-41
This gives
V =
V
* - /i)
From this the distance to any irregularity may be determined provided the difference
in frequency between two adjacent humps and the velocity with which an alternating
current flows along the line are known. The above equation may be written as
20* - /i)
Expressed in words this means that the distance to any irregularity equals the velocity
with which an alternating current flows along the line in question divided by twice the
difference in frequency between adjacent humps.
The velocity of transmission for all types of circuits is determined experimentally by
introducing a known irregularity and solving the equation for V. In practice it is usual
to take the difference in frequency between several adjacent peaks, between approximately
700 and 1500 cycles, and use the average difference in velocity at different frequencies
which causes the interval between peaks to change slightly with frequencj-.
Measurements are usually made with the simple form of impedance bridge shown sche-
matically in Fig. 12.
21. D-C AND LOW-FREQUENCY LINE TESTING
Telegraph, and telephone line test boards are generally equipped with special types
of voltmeters and Wheatstone bridges for making periodic tests of the line wires and for
the location of faults. These faults are of three general types: grounds, crosses, and
opens; and they may have any value of resistance from zero to several megohms. The
voltmeter provides a simple method of deter-
mining the type and magnitude of a fault, as
shown in Figs. 13, 14, 15, and 16.
Voltmeter
Une pair
.100,OOO-ohm voltmeter
Open at
distant end
Strap at
distaoi end
I? leakage is assumed uniform
-^-x length jn
Megohms per mile
FIG. 14.
Insulation Test
FIG. 13. Continuity Test
100,000-ohm voltmeter
T
-Open
.-
10V
raegolmrs
FIG. 15. High-resistance Leak to Ground
When key is closed the charging current will
cause a momentary deflection. The duration is
proportional to the capacitance. Thus by com-
paring the deflection obtained with the defective
wire with that obtained with a good conductor
of known length the distance to the fault can be
estimated.
FIG. 16. Voltmeter Test for Open
For the actual location of faults the Wheatstone bridge is used as illustrated in Figs.
17, 18, 19, 20, and 21. In these figures L is the length of the line and d is the distance
Good
Line
Strap
FIG. 17. Simple Bridge to Measure
Loop Resistance. At Balance RL — -R.
FIG. 18. Simple Murray Loop Test for Grounded
Conductor. When A and B are adjusted for
balance
11-42
ELECTRICAL MEASUREMENTS
from the testing end to the fault. It is assumed in the illustrations that the good and faulty
conductors used in the bridge measurement have the same resistances per unit length in
the case of grounds and crosses, and the same capacitances per unit length in the case of
opens.
Strap
Note: The conductor unit resistance will
not usually be accurately known. For this
reason a fault is ordinarily located on a per-
centage basis by making both simple loop and
Varley measurements.
FIG. 19. Simple Varley Loop Test for
Grounded Conductor
R
(K — ohms per conductor unit length.)
When R is adjusted to give minimum
response in telephone receiver
FIG. 20. Simple Murray Loop Test for
Opens. [Suitable only for short lines (1/2
mi cable). For longer lines use Fig. 21.
>Fault
Distributed capadlajoce I
^
Ry= resistance to balance
for capacitance of
length d of faulty
conductor
Ny= resistance to balance-
for resistance of
faulty conductor
sre capacitance
J_of good conductor of
~ length L
to balance, for capacitance
of length L
ti0=resistajice to balance for resistance
of 'good conductor
FIG. 21. To Locate an Open, a Bridge Reading Is Taken on the Open Conductor and Compared with
the Reading Obtained on a Good Conductor of Known Length
If the fault is a cross between wires, the second crossed wire is substituted for the ground
connection to the battery key.
It is important that the location be as accurate as possible to lessen the overall fault
clearing time, and to this end variations of the simple bridge tests are used to niinimize
errors (see references 22-29).
BIBLIOGRAPHY
1. Bennett, W. R., Cross-modulation Requirements on Multichannel Amplifiers below Overload,
Bell Sys. Tech. J., Vol. 19, 587-605 (October 1940).
2. Kinder, J. P., Measurement of Modulation in Carrier Amplifiers, Bell. Labs. Rec., August 1941.
3. Tidd, Rosen, and Wenk, New Test Equipment and Testing Methods for Cable Carrier Systems,
Trans. AJ.E.E., Vol. 66 (1947).
4. Bode, H. W., Network Analysis and Feedback Amplifier Desiffn, D, Van Nostrand. New York.
5. Black, H. S., Stabilized Feedback Amplifier, Bell Sys. Tech. J., Vol. 13, 1-18 (January 1934).
6. AJsberg and Leed, A Precise Direct Reading Phase and Transmission Measuring System for Video
Frequencies, BeU Sys. Tech. J., Vol. 28, 231-238 (April 1949).
7. Elliot, J- S., Precise Measurement of Insertion Phase Shift, Bell Labs. Rec., Vol. XVI, No. 8, 285.
8. Mead, S. P., Phase Distortion and Phase Distortion Correction, Bell Sys. Tech. J., Vol. 7, 195-224
(April 192S).
OVERALL A-M RECEIVES MEASUREMENTS 11-43
9. Lane, C. E., Phase Distortion in Telephone Apparatus, Bdl Sys. Tech. J., VoL 9, 493-521
(July 1930).
10. Nyquist, H., and Brand, S., Measurement of Phase Distortion, Bell Sys. Tech. J., Vol. 9, 522-549
(July 1930).
11. Wentz, J. F., Measuring Transmission Speed of the Coaxial Cable, Bell Labs. Rec.t June 1939.
12. Strieby, M. E., and Weis, C. L., Television Transmission, Proc. I.R.E., Vol. 29, 300-321 (July
1941) ; also p. 381.
13. Barstow, J. M., Blye, P. W., and Kent, H. 32., Measurement of Telephone Noise and Power Wave
Shape, Elec. Eng., Vol. 54, 1307-1315 (December 1935).
14. Castner, T. G., Dietze, E.r Stanton, G. T., and Tucker, R. S,, Indicating Meter for Measurement
and Analysis of Noise, Trans. AJ.E.E. , September 1931, pp. 1041-1047.
15. Schott, J. T., The Lookator, Bell Labs. Rec., October 1945, p. 379.
16. Abraham, Lebert, Maggio, and Schott, Pulse Echo Measurements on Telephone and Television
Facilities, Trans. A.I.E.E., Vol. 66, pp, 541 to 548.
17. Swift, G., Amplifier Testing by Means of Square Waves, Communications, February 1939.
18. Transient Response of a Broadcast System, General Radio Experimenter, April 1940.
19. Network Testing with Square Waves, General Radio Experimenter, December 1939.
20. Williams, J.T Square Wave Testing of Amplifiers, Radio JYetrs, January 1944, p. 24.
21. Ferris, L. P., and McCurdy, R. G., Telephone Circuit Unbalances, J. AJ.E.E., Vol. SLIII,
No. 12 (December 1924).
22. Palmer, W. T., A-c Method of Fault-localization in Telephone Cables, P.O.E.E. J., Vol. 23, No. 1
(April 1930).
23. Trans. AJ.E.E., Vol. 43, 423 and 1320.
24 Northrop, E. F., Methods of Measuring Electrical Resistance, McGraw-Hill, 1912.
25 Ritter, E. S., Cable Testing, Printed Paper 104, Institute of P.O.E.E., 1923.
26. Edwards, P. G., and Herrington, H. W., The Location of Opens in Toll Telephone Cables, Bell Sys.
Tech. J., Vol. 6, No. 1 (January 1927).
27 Henneberger, T. C., and Edwards, P. G., Bridge Methods of Locating Resistance Faults in Cable
Wires, Bell Sys. Tech. J., Vol. 10, 382-407 (July 1931).
28 Metson, G. H.T An Accurate Method of Sub-localizing Cable Faults, P.O.E.E. J., VoL 30, No. 2,
99 (1937).
29 Allan, J. M., Two Methods of Locating Cable Faults, P.O.E.E. JM Vol. 29, Part 2 (July 1946).
ROUTINE MEASUREMENTS ON A-M AND F-M
BROADCAST RECEIVERS
By W. O. Swinyard
In receiver measurements it is sometimes convenient to use the logarithm of the stage
gain so that gains can be added, instead of multiplied, to determine the overall non-
regenerative gain, and to express these in terms of decibels. It is also convenient to discuss
overall sensitivities in terms of decibels below 1 volt, in which case the microvolt sensitivity
is used to determine a voltage ratio. Though this is strictly a misuse of the term, it is
convenient and will lead to no serious difficulty as long as the user is aware of the limitations
of these practices.
, 22. OVERALL A-M RECEIVER MEASUREMENTS
REQUIRED TEST EQUIPMENT. Standard-signal generator, standard dummy
antenna, standard test loop, output wattmeter, audio-frequency generator, distortion
meter or wave analyzer, and an auxiliary 1000-kc signal generator.
STANDARD TEST CONDITIONS. Standard line voltage is 117 volts for a-c, d-c, and
a-c/d-c receivers. Receivers designed for a-c and d-c operation are usually tested on
alternating current and check measurements are made on direct current.
Measurements on automobile receivers should be made using a battery which provides
6.6 volts at the receiver battery terminals.
The normal test voltage for receivers designed for farm lighting systems is 36 volts.
Battery-operated receivers should be tested using new batteries of the type and voltage
specified by the receiver manufacturer.
The volume control and the tone control or controls should be set to provide maximum
400-cycle output. If a selectivity control is provided, it should be set, for the initial tests,
to provide greatest selectivity. The effect of the tone and selectivity controls on the per-
formance should be determined by special tests.
RECEIVER ALIGNMENT CONDITIONS. The overall sensitivity, selectivity, and
range,coverage of the receiver are first measured without disturbing the receiver alignment.
These measurements are followed by the single-stage measurements, after which the re-
ceiver is aligned, in accordance with the manufacturer's service instructions if available,
and complete overall measurements are made. Normally, no overall measurements are
made with the receiver aligned at each test frequency. However, in certain cases such
measurements might be desirable since they would show the effect of circuit misalignment
11-44
ELECTRICAL MEASUREMENTS
Standard
dummy
antenna
—
Receiver
>
Standard
dummy
load
1
y-
400-cycie
filter
t-
Harmonic
analyzer
1
Wattmeter
FIG. 1, Arrangement of Apparatus Used for Overall Measurements
on the overall sensitivity, assuming no regeneration. In all cases, however, the frequencies
at which the circuits are in. exact alignment should be noted.
Figure I shows the equipment as it is set up for overall measurements.
RANGE COVERAGE. The maximum and minimum frequencies to which the receiver
can be tuned in each band are recorded for the "as received" and later for the aligned
C°OVERALL SENSITIVITY (SENSITIVITY-TEST INPUT). This test normally con-
sists of determining the sensitivity-test input at three to six points in each wave band.
The output of the stand-
ard-signal generator is fed
into the input terminals of
the receiver through the
standard dummy antenna.
The output meter is con-
nected to the secondary of
the output transformer,
and the load is adjusted to
the proper value. The re-
ceiver is then turned on
and the voltage of the
power source set to the
correct value. After it
has throughly warmed up
it is tuned to the modu-
lated signal-generator out-
put and the controls are adjusted to provide maximum 400-cycle output. The 400-cycle
filter is then switched in to remove the noise, and the sensitivity-test input is determined.
It may be measured in decibels below 1 volt or in microvolts.
If the receiver employs a selectivity control its effect on the sensitivity is determined
by additional measurements which are usually made at 600 kc, 1000 kc, and 1400 kc.
The sensitivity of battery-operated receivers is measured in the normal^way and with
A and B batteries whose terminal voltage has dropped to 1.1 volts for the A and to 60
per cent of the nominal value for the B battery.
A 400-cycle filter used with the output wattmeter usually will reduce the noise voltage
in the output to a negligible level. However, there may be cases where noisy or extremely
sensitive receivers are being measured when allowance must be made for residual noise.
EQUIVALENT-NOISE-SIDE-BAND INPUT. The equivalent-noise-side-band input is
taken equal to the input of a single side band of 400-cycle modulation which will produce
an output from the receiver equal to the noise output, other conditions being the same.
The reason noise of both side bands has to be identified with a single-side-band component
of modulation is that there is a random-phase relation between the noise side bands as
distinguished from the specific phase relations existing between the carrier and each pair
of side-band components of modulation. The equation for JEN SI is: .
1? '
•En — 0.32?$ ~^~t
•&*
where En is the desired ENSI in microvolts, E8 is the carrier level in microvolts, Enr is
the rms output voltage of the noise alone with an unmodulated carrier applied ?to the
antenna, and Esf is the output voltage due to modulating this carrier 30 per cent at 400
cycles. The coefficient 0.3 is required because the test input is modulated 30 per cent, and
only one side band is considered.
To obtain ENSI, the sensitivity is first determined making due allowance for noise.
This gives a convenient value for E8 in microvolts. The corresponding 400-cycle output
voltage gives the value of Eaf. The modulation is then removed, the 400-cycle filter
switched out, and the rms voltage due to the noise is noted. This gives the value of En'
if a thermocouple meter is used or if the proper correction is applied for the particular
meter used. The corresponding ENSI may then be computed from the equation given
above.
The value of E/ and En' may be observed at a higher signal input level since only their
ratio enters. A good practice is to increase the carrier input at which ENSI measurements
are made, whenever the ratio En'/E8f exceeds 1 . This makes the effective increase in noise
power due to beats between noise side bands negligible relative to the power due to beats
between the noise side bands and the carrier.
It should be noted that it is possible to determine ENSI without using a 400-cycle
filter. Where this procedure is followed, it is convenient to set the attenuator to the point
OVERALL A-M RECEIVER MEASUREMENTS 11-45
which makes the noise-output power equal to the signal-output power. ENSI is then the
signal input multiplied by the per cent modulation.
SELECTANCE RATIOS. It is of interest to know how well the receiver discriminates
against signals located 10 kc away on either side of the desired channel. The regular overall
sensitivity setup is used. The selectance ratio in decibels is the difference between the
.signal input in decibels below 1 volt required for normal test output on the channel to
which the receiver is tuned and that required for normal test output on the adjacent
channel. The selectance ratios are usually measured at 600 kc, 800 kc, 1000 kc, and 1400
kc in the broadcast band and at corresponding points in the long-wave band if one. is used.
IMAGE RATIOS. The setup for these measurements is the same as that for overall
sensitivity. After measuring the sensitivity, the receiver tuning is left undisturbed and
the signal generator is set to the image frequency. The least signal-input voltage with the
signal modulated 30 per cent at 400 cycles required for normal test output is the image
sensitivity. The image ratio in decibels is the difference between the overall and image
sensitivities, when both are expressed in decibels below 1 volt.
There are other spurious responses such as the half i-f image which are due to oscillator
harmonics beating against either the fundamental of an interfering signal or harmonics
of that signal which may be generated in the receiver. However, these are not usually
measured in a routine receiver analysis.
I-F REJECTION RATIOS. The sensitivity of the receiver to the intermediate fre-
quency is determined with the regular setup used for overall-sensitivity measurements
(including the standard "all-wave" dummy antenna). The i-f rejection ratio in decibels
is the difference between overall and i-f sensitivities in decibels below 1 volt. Measure-
ments are usually made at three points in each wave band. In the broadcast band these
points are usually the two lowest and the highest frequency test points.
OVERALL SELECTIVITY. The overall selectivity is measured at the center of the
band (1000 kc in broadcast receivers). The setup is the same as that used for overall-
sensitivity measurements, and the measurement can conveniently be made after the
measurement of sensitivity and ENSI at 1000 kc. The total widths of the selectivity
curve at points 6, 20, 40, 60, and 80 db down from the resonant voltage peak are recorded
in kilocycles as We, W%» 1^40, Weo, and W&. The procedure is as follows: the receiver is
tuned to resonance at 1000 kc and the attenuator set to the sensitivity-test input; the
signal generator is then tuned off resonance and the output voltage is increased 6 db; the
generator is tuned toward resonance until normal test output is secured and the frequency
is noted; the generator is then tuned through resonance to the point on the other side where
normal test output is secured and the frequency is again noted. The difference in kilo-
cycles between these two readings is W& For WM, W&, etc., the process is repeated. At
this point it should be pointed out that the modulation should be removed while the
generator is tuned through resonance to avoid damage to the output meter and that care
should be taken to avoid errors in the measurement due to possible back-lash in the signal
generator frequency-dial mechanism.
Where variable i-f selectivity is employed, selectivity measurements are usually made
at each position of the selectivity control switch, or at three positions, in the case of
continuously variable selectivity, at the extremes and middle settings of the control.
An additional measurement of selectivity is made in the case of battery-operated re-
ceivers, namely, under the ''dead battery" conditions previously described.
For a receiver employing a long-wave band, it is desirable to measure the selectivity at
the midpoint of this band since the normal selectivity of low-frequency preselector circuits
may result in appreciable narrowing of the skirt selectivity.
In the case of a receiver incorporating a double avc system normal selectivity measure-
ments will indicate sharper selectivity than is actually provided by the selectivity of the
resonant circuits. This is true to some extent in any receiver which has less selectivity to
the avc detector than to the signal-frequency detector. In some cases it may be advisable
to disable the avc before making selectivity measurements.
WHISTLE MODULATION. When a signal having a frequency close to twice the
intermediate frequency is being received it is often accompanied by an audible whistle or
tweet. This is measured at several values of signal-input level and compared with the
corresponding 400-cycle modulated signal by expressing the whistle in terms of the per
cent modulation at 400 cycles required to give an output voltage equal to that resulting
from the whistle.
Measurement of the equivalent whistle modulation is made with the regular setup for
overall-sensitivity measurements. The signal generator with the output set to the appro-
priate value and with zero modulation is tuned to approximately twice the intermediate
frequency. The exact setting is chosen by slowly turning the generator from about 30 kc
below to 30 kc above the frequency that is twice the intermediate frequency while the
11-46 ELECTRICAL MEASUREMENTS
receiver timing control is rocked. The generator is set at the point providing the greatest
whistle output. The receiver, not the generator, is detuned to produce a whistle of max-
imum intensity to the ear, the volume control being set so that the output voltage at this
point is well below the overload level. The 400-cycle filter is then switched in; the modula-
tion is applied to the signal generator and adjusted until the output approaches as closely
as possible the output previously noted. The ratio of the 400-cycle output voltage to the.
whistle voltage multiplied by the per cent modulation gives the whistle modulation in per
cent. This procedure is followed for inputs of 0, 20, 40, and 60 db below 1 volt.
The above procedure must be modified when measuring the whistle modulation at input
levels of 80 db below 1 volt and less, since the noise tends to mask the whistle when the
filter is not used. Therefore, the 400-cycle filter is switched in and the whistle^ carefully
adjusted to give maximum output. Then the receiver is tuned slightly to one side of the
carrier, the modulation applied, and the whistle modulation determined as before. The
equivalent whistle modulation measured at 400 cycles is usually substantially less than that
of higher frequency whistles, when appreciable avc voltage is developed. However, these
low-level measurements are usually only important qualitatively, and they indicate the
need for work on the receiver to remove their causes. In thoroughly shielded receivers of
correct design the whistle is usually not measurable with inputs below 80 db below 1 volt.
OUTPUT AND AVC CHARACTERISTICS. These measurements are made in the
middle of the band (1000 kc for broadcast receivers) using the setup and test conditions
for overall sensitivity. The signal is modulated successively at 0, 10, and 30 per cent for
each value of signal input. The signal input is varied from 120 db to 0 db below 1 volt,
and the audio output for each of the three modulation percentages is plotted against the
corresponding signal input. The 400-cycle filter is switched in to remove the noise from
that portion of the 30 per cent curve which is below the overload level, and the data are
recorded with and without the filter for this portion of the curve. The 0 per cent output
curve indicates the noise output of the receiver at full sensitivity. It also indicates the
presence of hum modulation and motorboating at high signal-input levels.
The avc characteristic is taken in the same manner as the 30 per cent modulation curve
except that the volume is reduced sufficiently to prevent overloading the output amplifier.
Usually a reduction in the output voltage of 6 db with a 0 db below 1 volt signal input is
sufficient. The 400-cyele filter should be used where a measurable amount of noise is
present.
AVC FIGURE OF MERIT. The avc figure of merit can be obtained from the avc char-
acteristic. It is the number of decibels decrease in signal input necessary to reduce by 10
db the output obtained at a signal input level of 20 db below 1 volt.
TWO-SIGNAL SELECTIVITY (CROSS-TALK INTERFERENCE). For these meas-
urements the generators may be coupled to the receiver under test in either a series or
parallel arrangement. The measurement is made at 1000 kc for two values of desired signal
input: 46 db and 0 db below 1 volt for home receivers and 46 db and 14 db below 1 volt
for automobile receivers. The 1000-kc signal is tuned in with the volume control set to
provide a medium-strength a-f output from a 1 per cent modulated signal. Modulation
is then removed; the two generators are connected together with the interfering signal
modulated 30 per cent and introduced at amplitudes which result in the output previously
noted for the 1 per cent modulated desired signal. The interfering signal measurements
are taken at every channel on both sides of 1000 kc up to a 100-kc difference unless the
necessary signal input reaches the maximum output of the generator before the plus and
minus 100-kc points have been reached.
If an auxiliary 1000-kc generator is used, the necessary output adjustments can be made
using the standard-signal generator modulation for both desired and interfering signals.
When the two are connected in series for the test the auxiliary 1000-kc generator, having
no modulation, serves as the desired signal.
It should be noted that the impedances of the two standard dummy antennas which are
necessary if the signal generators are connected in parallel should be double the normal
values. If the two generators have equal output impedances independent of the attenuator
settings, the effective output voltage produced by either one is only half the indicated
output.
In making the two-signal selectivity tests two whistles will usually be encountered on
the low-frequency side of 1000 kc. If the intermediate frequency is 455 kc, the first occurs
at approximately 955 kc and is due to the beat between the fundamental of the receiver
oscillator, 1455 kc, and the second harmonic of the input signal. The second occurs at
approximately 910 kc and is the regular twice-i-f whistle to which previous reference has
been made.
HARMONIC DISTORTION. A distortion analysis is made at 1000 kc using the setup
for overall sensitivity in conjunction with a distortion meter or a wave analyzer. Three
OVERALL A-M RECEIVER MEASUREMENTS 11-47
sets of measurements of per cent harmonics are made. For the first the signal input is
maintained constant at 46 db below 1 volt, with 30 per cent modulation at 400 cycles.
Harmonics are measured at several output levels up to and including the maximum obtain-
able. It is desirable to choose one output level so that 10 per cent total distortion results
since this is usually chosen as representing the maximum undistorted output. For the
second set of measurements the signal input is maintained constant at 46 db below 1 volt
and the receiver volume control is adjusted for normal test output. The modulation is
then set to 10 per cent, 50 per cent, and SO or 100 per cent, and the harmonics are measured
for each value of modulation percentage. The final measurements are made keeping the
modulation at 30 per cent, the output at normal test output, setting the signal-input level
to 60 db, 40 db, 20 db, and 0 db below 1 volt and measuring the harmonics at each value
of signal input. These values of signal input may have to be modified for receivers of
special types. If a wave analyzer is used the total per cent harmonic distortion is calculated
as the square root of the sum of the squares of the individual per cent harmonics.
OVERALL ELECTRICAL FIDELITY, The regular avera]l-sensitivity-measurement
setup is used for this measurement except that the signal generator is modulated 30 per
cent by an a-f signal generator of variable frequency and the 400-eyele filter is switched
out. The receiver is first tuned to 1000 kc using a weak signal. The signal input is then
set to 46 db belo\v 1 volt, and the receiver volume control is set to provide an output well
below overload. The modulation frequency is then increased until the output is reduced
by about 14 db, and the tuning control is finally adjusted for minimum output at this
frequency. The modulation is then set back to 400 cycles and a final adjustment of the
output voltage is made. The output is then measured at a sufficient number of modulation
frequencies to permit plotting a curve showing the relative response, in decibels, versus
modulation frequency using the 400-cycle output voltage as a reference. Curves are
made showing the maximum overall fidelity and the effect of the tone control on the
fidelity. Usually two curves are recorded: (1) with the tone control set ics maximum highs,
and (2) with the tone control set for minimum highs, In the case of 1.4r-volt battery-
operated receivers the fidelity is also measured using "dead batteries." If a bass-com-
pensated volume control is used, measurements should be made with the arm set both
above and below the tap to show the effect of the bass compensation. It may be better
to disconnect the network from the tap in order to avoid overload.
TESTS ON PUSH-BUTTON TUNERS. Receivers provided with a mechanical push-
button tuning mechanism are subjected to tests devised to show how accurately the push
buttons can be set and how well they return to the frequency to which they are set. For
these tests the buttons are all set up to tune a signal near the high-frequency end of the
band to zero beat with a signal from another generator which is set to the intermediate
frequency. For each push button the gang is opened, the button actuated, and the re-
sultant beat recorded as a frequency error. This is repeated several times, usually eight,
and similar tests are made from the closed position of the gang. Finally tests are made
with the gang alternately opened and closed before the button is pushed. All measure-
ments for each button (24) are then averaged taking account of the sign, and the result is
recorded as a setting error. The setting errors for each button are averaged without
regard to sign to secure the average setting error. The deviations of all the errors for each
button from the figure represent ing the setting error for that button averaged without
regard to sign give the mean tuning deviation. The average mean tuning deviation is
the average of the mean tuning deviations.
MEASUREMENTS USING STANDARD TEST LOOP. The following measurements
which employ the standard test loop (Fig. 2) are made on loop receivers: sensitivity,
Tubular shield
10'7in diameter
_£03-ohm resistor
hoosktg
FIG. 2. Test Loop
11-48 ELECTRICAL MEASUREMENTS
JSNST image, i-f and selectance ratios, and loop figure of merit. The test loop is connected
to the output of the signal generator and set up 24 in. away from the receiver loop with
the loops arranged coaxially. The overall sensitivity in decibels below 1 volt per meter is
20 db below the signal generator attenuator reading when the input is adjusted for normal
test output. The loop figure of merit is the difference between the sensitivity in decibels
below 1 volt per meter and the sensitivity at the first grid measured in decibels. It is
recorded as minus when the absolute magnitude of the overall sensitivity in decibels below
1 volt per meter is less than the first grid sensitivity in decibels. Where no external
antenna connection is provided other measurements than these must of necessity be made
using the loop input. In all cases the same procedure is followed as has been previously
outlined except that the input is specified in decibels below 1 volt per meter. Many signal
generators operated with the standard test loop will not provide an input to the receiver
loop of more than 20 db below 1 volt per meter when the test loop is operated under normal
conditions.
AUDIO FEEDBACK FACTOR. If the audio amplifier of the receiver employs negative
feedback a measurement of overall a-f gain is made with the feedback removed, and the
increase in gain measured in decibels at 400 cycles is expressed as the audio feedback factor.
OSCILLATOR DRIFT. This test may be carried out as follows: The receiver is tuned
to a secondary frequency standard or to a signal generator of known stability character-
istics. The resultant beat produced as the oscillator drifts is measured by zero beating it
against an audio signal from an amplifier fed by an a-f generator. Oscillator drift measure-
ments are made at some point near the high-frequency end of each band. The receiver
is tuned to about the right point and then turned on and as quickly as possible tuned to
zero beat against the frequency standard or signal generator. Measurements are made
every 5 minutes for a half hour and then every 15 minutes for 2 hours or until the oscillator
frequency has become stabilized. If the oscillator drift is such that the beat note goes above
the range of audibility the drift can be determined directly by zero beating with the
signal generator for each measurement. The direction of drift can be determined by noting
the effect on the beat note of a small change in the capacitance in the oscillator tank
circuit — a change such as is produced by bringing a finger up close to the tuning condenser
stator.
23. SINGLE-STAGE MEASUREMENTS
REQUIRED TEST EQUIPMENT. Standard-signal generator, standard dummy
antenna, output wattmeter, vacuum-tube voltmeter, tuning wand, reactance meter or Q
meter, high-resistance voltmeter, and a wattmeter.
HIGH-FREQUENCY MEASUREMENT PRECAUTIONS. In many cases measure-
ments cannot be made properly by substituting a vacuum-tube voltmeter for a tube or
by placing it in parallel with a tube. The inherent capacitance of the stage may be so low
that a change in its value may decidedly influence the shape of the selectivity curve. In
such cases it is suggested that the procedure to be described later for use in making single-
stage measurements on f-m receivers be followed.
ANTENNA GAIN AND BAND WIDTH. The voltage gain from the antenna to the
first grid is measured at all the test frequencies used for sensitivity measurements. The
width of the resonance curve 6 db down is measured at three points in each wave band.
For these measurements the signal generator output voltage unmodulated is fed into the
receiver antenna circuit through the standard dummy antenna. The voltage developed
across the output of the antenna circuit is measured by means of a vacuum-tube voltmeter
to which the lead normally connected to the grid of the first tube is connected. The signal
generator output voltage is increased by 6 db and the generator is then detuned on each
side of resonance until the output drops to the reference value. If there are two tunable
circuits ahead of the first tube the gain and band widths are also measured on the first
circuit alone. Where measurements are made at high frequencies, the precautions previ-
ously noted must be observed.
COIL MISALIGNMENT. When there are two tunable circuits ahead of the first tube
or an antenna and an r-f stage, the misalignment of these circuits can be measured by
means of a reactance meter or a Q meter. For a receiver with a tuned r-f stage, the re-
ceiver tuning condenser is set at a minimum capacitance and the standard dummy antenna
is connected across the antenna-ground terminals of the receiver. The r-f circuit is used
as a standard and connected across the condenser terminals of the Q meter, with a standard
coil <5overing the desired range plugged into the coil terminals. The frequency of the Q
meter is set to the high-frequency alignment point and the Q meter condenser adjusted
for maximum Q indication. The antenna circuit is then substituted for the r-f circuit and
ibe antenna trimmer adjusted to bring the antenna circuit into exact alignment with the
r-f circuit as indicated by a maximum reading on the Q indicator.
SINGLE-STAGE MEASUREMENTS 11-49
After the antenna and r-f circuits have been aligned, the Q meter is set to each of the
test frequencies and at each point the r-f circuit is connected to the condenser terminals
and the Q meter tuning condenser is adjusted for maximum Q indication. The antenna
circuit is then substituted for the r-f circuit and the Q meter condenser is readjusted for
maximum Q indication. The difference between the two condenser settings is the misalign-
ment correction in micromicrofarads between the two circuits.
Another measurement is made using the Q meter to determine the effect changing the
antenna capacitance has on the broadcast or long-wave band tuned antenna circuit. For
these measurements the receiver tuning condenser is set to minimum capacitance and the
condenser terminals of the Q meter are shunted across the tuned antenna circuit. A
dummy antenna, identical to the standard dummy antenna except that the series capaci-
tance element is adjustable, is set to the standard value of 200 pid and connected across
the antenna input circuit. The Q meter is set to 500 ke, and the Q meter condenser is
adjusted for maximum Q indication. The antenna capacitance is then set to 60 /*/if,
100 /A/if, 300 /A/if, 500 wf, and short circuit (infinite capacitance), and the alignment
corrections are noted for each value of antenna capacitance. These measurements are
usually made at 500 kc, 600 kc, 700 kc, 1000 kc, and 1400 kc for the broadcast band in
cases where a high-inductance antenna primary is used. The 700-kc and 1000-kc points
may be omitted if the alignment is good. If the antenna circuit employs a low-inductance
primary, resonant above 1500 kc, the test points are usually 600 kc, 1000 kc, 1200 kc,
1400 kc, and 1500 kc. In this case the 1000-ke and 1200-kc points may be omitted if the
alignment is good at 1400 kc. Corresponding values are used in the long-wave band if
one is provided. In the case of receivers intended to operate with antennas having char-
acteristics substantially different from normal, values of antenna capacitance appropriate
to the case are chosen instead of the above-mentioned values.
ALTERNATIVE METHOD OF MEASURING ALIGNMENT OF PRESELECTOR
CIRCUITS. To remove the possibility of error due to regeneration the avc line is biased
by means of a battery, 4 1/2-9 volts will usually be sufficient. AH circuits are then aligned
in accordance with manufacturer's service instructions. At each test frequency the mis-
alignment of the preselector circuits can be determined by means of a "tuning wand,"
which consists of a length of insulating rod, such as hard rubber or Bakelite, to which an
iron-dust slug and a brass slug are attached, one at each end. This is held inside or near
each preselector coil. If the output of the receiver decreases when either the brass or the
iron is brought near the coil, no misalignment exists. However, if either end causes an
increase in output the misalignment is equal to the decibel increase in sensitivity. If the
increase is caused by the brass, the coil inductance is too high; if it is caused by the iron,
the inductance is too low.
R-F STAGE MEASUREMENTS. The voltage gain from the grid of each r-f amplifier
stage to the grid of the following stage is measured at all the regular test frequencies, and
the 6-db band width is measured at three points in each band as discussed in the section
covering antenna circuits. The output of the signal generator is fed into the grid of the
tube incorporated in the stage being measured, and a suitable vacuum-tube voltmeter is
connected to the lead which normally is connected to the following grid. When the signal
generator is connected so as to replace a grid circuit which normally returns to the avc
string it should be connected through a condenser, with a grid leak returning to the avc
circuit so as to maintain normal bias on the tube. The grid leak is returned to the avc
circuit even though the avc may eventually return to ground, since otherwise the measure-
ments may be in error owing to the initial avc voltage caused by space current due to the
emission velocity of electrons from the diode cathode.
I-F MEASUREMENTS. Diode Stage. The diode stage gain is measured by connect-
ing the vacuum-tube voltmeter from the diode plate to ground, thus not appreciably
disturbing the loading on the diode transformer. The signal generator output is connected
through the previously mentioned condenser-grid leak combination, to the last i-f grid,
and the stage is aligned for maximum output. A measurement of the voltage gain of the
stage is then made, and the bandwidths 6 db and 20 db down are determined.
I-F AMPLIFIER STAGE GAIN AND BANDWIDTHS. Measurements of gain and
bandwidths of i-f stages are made as described above except that the vacuum-tube volt-
meter is not shunted across the grid circuit of the following tube; it replaces it. It often
is advisable to isolate the vacuum-tube voltmeter by means of a high-resistance grid leak
and condenser if these elements are not incorporated in the instrument.
MODULATOR STAGE GAIN AND BANDWIDTHS. This measurement is made in
the manner described in the above paragraph. The signal-frequency circuits should be
set to the middle of the band and the oscillator should be operating for this measurement.
CONVERSION GAIN. The connections for the signal generator and vacuum-tube
voltmeter used in measuring the gain of the modulator stage are employed to measure
conversion gain, the only difference being that the signal generator is set to the standard
11-50 ELECTKICAJO MEASUREMENTS
test frequencies in each band, conversion gain being denned as the ratio of rms voltage
of intermediate frequency at the grid circuit terminals of the first i-f transformer to the
rms voltage of signal frequency applied at the grid of the modulator tube. The avc system
should be disabled for these measurements.
SENSITIVITY ON MODULATOR AND ON I-F GRIDS. The least signal input to the
last i-f grid required to produce normal test output with the signal modulated 30 per cent
at 400 cycles is called the i-f sensitivity. A corresponding measurement made from the
modulator grid is called the modulator-grid sensitivity. The i-f circuits should be aligned
in both cases.
DETECTOR SENSITIVITY. The detector sensitivity is denned as the amplitude of
the 30 per cent modulated rms voltage which must be applied to the detector tube to
produce normal test output. It is of course an indication of the total a-f gain. It is usually
determined indirectly from the measured diode stage gain and the sensitivity on the last
i-f grid, the difference between these two quantities being the detector sensitivity in decibels
below 1 volt.
OSCILLATOR VOLTAGE. The oscillator voltage usually measured is the d-c voltage
across the oscillator grid leak, as calculated from the measured resistance value of the grid
leak and the measured current flowing through it when the oscillator is working. The
voltage is measured at each test frequency throughout the range of the receiver. If the
oscillator circuit necessitates some other method of measuring oscillator voltage, the pro-
cedure followed should be noted.
24. MISCELLANEOUS MEASUREMENTS ON A-M RECEIVERS
HUM VOLTAGE. The rms value of the hum in the output of the receiver can be
determined by means of the output meter, provided sufficient sensitivity is available, or
by connecting the primary of a voltage step-up transformer across the primary of the
output transformer. The voltage measured across the secondary of this transformer by
means of a vacuum-tube voltmeter is divided by the transformer voltage ratio to get the
required value of hum in the output circuit. The voice coil should be connected for this
measurement. The hum should be measured for both the maximum and the minimum
settings of the volume control. To prevent receiver noise from interfering with the
measurement a large condenser should be connected from the plate of the last i-f tube to
the B+ line.
MINIMUM OUTPUT SIGNAL. This measurement is made to determine how close
to zero output the volume control can reduce the signal. The receiver is tuned to a 1000-kc
46-db below 1 volt signal 30 per cent modulated, and the power across the standard dummy
load is measured. The 400-cycIe filter should be used to remove hum and noise.
CONDENSER GANG ALIGNMENT. In the case of gangs having uniform sections
the corrections in micromicrofarads required to bring the antenna and/ or r-f sections into
alignment with the oscillator section are measured for several settings of the condenser
gang. If these measurements exceed normal tolerances the gang can be knifed to make
the necessary changes.
D-C VOLTAGES. The principal d-c potentials existing at the tube elements should be
measured using a high-impedance voltmeter, preferably an electronic voltmeter, and tabu-
lated. These measurements are made directly after the "as received" measurements and
at standard line or test voltage.
POWER CONSUMPTION. The power consumed by the receiver at standard line or
test voltage is measured by means of a suitable wattmeter. In the case of battery-operated
receivers the A and B drains should be measured.
25. F-M RECEIVER MEASUREMENTS
Measurement of such characteristics as antenna and r-f gain and selectivity, i-f gain
and selectivity, etc., is independent of the type of modulation which the receiver is designed
to receive, hence the methods described above are applicable. In the case of f-m receivers,
higher frequencies are involved; hence, the high-frequency measurement precautions to
be described later must be observed.
EQUIPMENT. The equipment required for routine measurements on a-m receivers
is usually required for f-m receivers, since relatively few are designed solely for frequency
modulation. Generally, frequency modulation is one of several frequency bands incor-
porated in a receiver. Only measurements such as quieting and deviation sensitivity, etc.,
where f-m modulation of the signal generator is required, necessitate the use of an f-m
signal generator.
OVERALL PERFORMANCE TESTS 11-51
DEFINITIONS OF TERMS. See also Standards on Radio Receivers, 1947, I.R.E.,
Methods of Testing Frequency Modulation Broadcast Receivers.
Standard Very-high-frequency Dummy Antenna. The very-high-frequency dummy
antenna is a pair of resistors, one connected in series with each terminal of the signal
generator, of such value that the total impedance between terminals, including the signal
generator, is 300 ohms "balanced to ground.
Standard De-emphasis Characteristic. The standard de-emphasis characteristic has a
falling response with modulation frequency, the inverse of the standard pre-emphasis
characteristic, equivalent to that provided by a simple circuit having a time constant of
75 microseconds. The characteristic may be obtained by taking the voltage across a
condenser and resistor connected in parallel and fed with constant current. The resistance
in ohms is equal to 0.000075 divided by the capacitance in farads. The standard de-
emphasis characteristic is incorporated in the detector and/or audio circuits of the receiver.
Standard Test Frequencies. The standard test frequencies used in testing f-m receivers
are 88, 98, and 108 megacycles. If more than three frequencies are required, it is suggested
that 93 and 103 megacycles be included. If only one test frequency is needed, 98 mega-
cycles should be used.
Standard Test Modulation, This term refers to a signal that is frequency modulated at
400 cycles with a deviation of 30 per cent of the maximum system deviation of 75 kc. The
deviation due to standard test modulation is therefore 22 1/2 kc.
Maximum-sensitivity Test Input. The maximum-sensitivity test input is the least
input signal of a specified carrier frequency having standard test modulation which, when
applied through the verv,-high-frequency dummy antenna, results in standard test output
when all controls are adjusted for greatest sensitivity. It may be expressed in terms of
power in decibels below 1 watt, in decibels below 1 volt, or in microvolts. Generally it
is advisable to use a 400-cycle filter to remove the noise from the output.
Maximum-d elation-sensitivity Test Input, The ma^imiirn-deviation-sensitivity test
input is the least input signal of a specified carrier frequency having full rated system
deviation which, when applied to the receiver through the very-high-frequency dummy
antenna, results in 10 per cent distortion in the output when the volume control is adjusted
to standard output. It is expressed in decibels below 1 watt, in decibels below 1 volt, or
in microvolts.
Deviation-sensitivity Test Input. The deviation sensitivity test input is the minimum
deviation at 400 cycles of a carrier of 60 db below 1 volt required to give maximum undis-
torted output when all controls are adjusted for greatest sensitivity. The deviation sensi-
tivity is expressed in kilocycles or as a percentage of maximum full system deviation.
Quieting-signal-sensitivity Test Input. The quietrng-signal-serisitivity test input is
the least unmodulated signal input which, when applied to the receiver through the very-
high-frequency dummy antenna, reduces the internal receiver noise to the point where the
test output rises 30 db when standard test modulation is applied to the input signal, the
volume control being adjusted to avoid audio overload. It is expressed in decibels below
1 watt, in decibels below 1 volt, or in microvolts.
26. OVERALL PERFORMANCE TESTS
The setup for overall performance tests is the same for f-m receivers as for a-m receivers,
assuming that in each case an appropriate signal generator and standard dummy antenna
provide the test signal. For measurements on f-m receivers a resistor having a value equal
to the input impedance for which the receiver was designed may be used as a dummy
antenna. If the receiver employs a balanced input, half the resistance is used in each side.
The conditions set down on p. 11-43 regarding receiver alignment apply here also.
OVERALL SENSITIVITY. The sensitivity-test input for the maximum sensitivity,
the maximum deviation sensitivity, the quieting-signal sensitivity, and the deviation
sensitivity should be measured at 3 to 6 frequencies.
IMAGE AND I-F RATIO S- The procedure for determining these characteristics is the
same as for a-m receivers. The maximum-sensitivity test input should be used in deter-
mining the image and i-f sensitivity.
OUTPUT AND AVC CHARACTERISTICS (LIMITER CHARACTERISTICS). This
measurement corresponds to the output and avc characteristics of a-m receivers, and the
same procedure is followed in obtaining the data. In the case of f-m receivers, the modula-
tion percentages used are 30 per cent (22 1/2 kc) and 10 per cent (7.5 kc). The output
power versus signal-input voltage is determined at 98 megacycles for maximum setting
Of the volume control. The limiter or avc characteristic is measured with &0 per cent
modulation at a volume control setting which gives 6 db less than the mnTimnm output.
The output versus input for zero modulation is also determined.
11-52
ELECTKICAL MEASUREMENTS
HARMONIC DISTORTION. The measurements of harmonic distortion required for
an f-m receiver are as follows: per cent harmonics versus per cent modulation and per
cent harmonics versus signal-input level and per cent harmonics versus output.
OVERALL ELECTRICAL FIDELITY. The overall electrical fidelity is measured at
98 megacycles using a signal input 60 db below 1 volt, 30 per cent modulated. The curve
thus obtained should normally be a close approximation to the standard de-emphasis curve
for f-m receivers assuming no pre-emphasis in the signal generator. If the receiver is multi-
band, the effects of the tone controls will be shown by the fidelity measurements on the a-m
bands; otherwise, additional data should be taken to show these effects on the fidelity.
I-F AMPLIFIER CHARACTERISTICS. The overall selectivity of the i-f amplifier
from the modulator grid to the first limiter grid or, if limiters are not employed, to the
plate of the detector driver tube, is measured after the individual stage gain and selectivity
have been measured. The level at the limiter grid should be that required for quieting
the receiver. Where avc voltage is applied to i-f amplifier stages, the overall i-f amplifier
selectivity characteristics should be measured for different levels of signal input to the
modulator grid in order to show the detuning effect due to the change in tube input capaci-
tance with a change in grid bias. Typical input levels are 80 db, 60 db, and 40 db below 1
volt. The avc voltage in the circuit should be held at the center frequency level by means
of a battery supply.
27. SINGLE-STAGE MEASUREMENTS
REQUIRED TEST EQUIPMENT. Standard-signal generator, standard dummy
antenna, output wattmeter, vacuum-tube voltmeter, tuning wand, high-resistance volt-
meter, and wattmeter.
HIGH-FREQUENCY MEASUREMENT PRECAUTIONS. It will usuaUy be found
impracticable in making stage gain measurements on f-m receivers to substitute a vacuum-
Rr.H tube voltmeter for a tube or
to place it in parallel with a
tube. The inherent capaci-
tance of the stage is usually so
low that accurate measure-
ments cannot be made if the
measurement setup appreci-
ably changes its value. A
preferred method is as follows
(Fig. 3) : A resistor of approxi-
mately 500 ohms is substi-
tuted for the normal plate
load of the tube which the
vacuum-tube voltmeter
would replace at lower fre-
quencies. Under most condi-
tions it is inadvisable to shunt
this resistor across the normal
plate load. The low-potential
end of the resistor is by-
passed directly to ground,
keeping lead lengths as short
as possible. The signal gener-
ator is then connected to the
grid of the tube, the normal
grid load being disconnected,
and a vacuum-tube voltmeter
is connected across the resis-
tor in the plate circuit. The
input-output voltage charac-
teristic can then be checked
and a suitable operating point
chosen on the linear portion
of the gain characteristic.
With the suggested value of
load resistance and the usual
high-transconductance tube,
a gain of 0-6 db will be se-
cured.
B-f
A.V.6.
FIG. 3.
B, calibrating rf
e Measurement Set-up. A, normal circuit;
e; C, set-up for measurement of antenna gain
and bandwidths.
SINGLE-STAGE MEASUREMENTS
11-53
Under these conditions it will be convenient to select as a reference output voltage that
value which corresponds to a signal on the grid of 10 db below 1 volt. It is important that
the voltmeter have sufficient sensitivity to make possible the selection of an operating
point which can be obtained without danger of grid current due to high signal levels on
the grid. After the operating point has been chosen, the grid of the tube can be connected
back in the circuit, the signal generator connected to the grid of the preceding tube, and
performance measurements made without upsetting the grid loading in the stage being
measured.
ANTENNA GAIN AND BANDWIDTHS. The measurement of antenna gain and
band width to provide data representative of those secured under actual operating condi-
tions requires considerable care. If the first tube is a pentode r-f amplifier, antenna gain
and band widths may be measured by placing the voltmeter across a resistive plate load
of a few hundred ohms and then calibrating the tube as previously described. The data
may then be secured without upsetting actual operating conditions.
If the antenna secondary feeds into the grid of the converter tube, it may not be possible
to measure antenna gain separately. In such cases, it is usually possible to measure the
gain from the antenna terminals to a resistive load in the plate circuit of the i-f amplifier
tube. In this way the sum of the antenna gain and conversion gain can be obtained. If
it is possible to measure the conversion gain separately, the antenna gain can be obtained
indirectly by subtraction of the conversion gain.
R-F GAIN AND BANDWIDTH. The method of measurement of r-f gain, like that of
the measurement of antenna gain, depends to a great extent on the type of circuit. In
some cases, the voltmeter can be shunted across the grid of the modulator tube to enable a
measurement of r-f gain to be made. In others, it is necessary to measure the r-f gain plus
the conversion gain as has been discussed under the immediately preceding heading. It
is always necessary to exercise care to make sure that the loading on the r-f tuned circuit
under measurement conditions is the same as that under actual operating conditions.
CONVERSION GAIN. Conversion gain measurements where a pentagrid converter
is used can generally be made by placing the vacuum-tube voltmeter across a resistive
load in the i-f plate circuit as has previously been discussed for antenna and r-f gain
measurements. Where a pentode modulator is used with both oscillator and signal voltages
on the same grid, it is necessary to measure conversion gain indirectly. The antenna gain
plus conversion gain or r-f gain plus conversion gain can be measured. The antenna gain
or r-f gain, as the case may be, can then be measured and subtracted to give the conversion
gain. As usual, in making measurements at these frequencies, care must be exercised so
as not to allow the measurement setup to change the loading on the antenna coil.
I-F GAIN AND BANDWIDTH. The measurement of i-f gain and band width at the
standard intermediate frequency of 10.7 megacycles can best be made by placing the
vacuum-tube voltmeter across a resistive load in the plate circuit of the tube following
the stage on wjiich measurements are being made. The tube can then be calibrated and
the measurements made without upsetting actual operating conditions.
REJECTION OF A-M BY F-M DETECTOR. No measurement has yet been standard-
ised for this test. However, Fig. 4 shows one method for setting up equipment in a way
which will provide useful
information regarding the
ability of an f-m detector
to reject amplitude modu-
lation. Imperfect a-m re-
jection at any signal input
level will result in the
"bow-tie" pattern. For
this test the f-m signal
generator must be capable
of being simultaneously
amplitude- and frequency-
modulated. The a-m and
f-m frequencies should be
asynchronous. It is sug-
gested that the f-m fre-
quency be approximately
100 cycles and that the
a-m frequency be approxi-
mately 400 cycles.
OSCILLATOR DRIFT.
The frequency drift of an
f-m receiver oscillator cir-
FIG. 4. Equipment Set-up for Test of A-m Rejection in F-m De-
tectors
11-54 ELECTRICAL MEASUREMENTS
cuit may be determined by employing the equipment setup shown in Fig. 5. The procedure
is as follows:
1. Tune the receiver to the 100-megacycle signal from the crystal oscillator.
2. Adjust the frequency and level to
produce zero beat in the output.
3. Maintain aero beat by adjusting the
frequency of the signal generator. Note
frequency drift versus time until the re-
ceiver has stabilized.
^-Q-7 Mc MISCELLANEOUS MEASURE-
MENTS. There are several character-
istics for which measurement procedures
have not yet been standardized. These
• AocTto include oscillator radiation, effect of de-
, ( , I outpcrf tuning, two-signal interference tests, tests
Fro. 5. Oscillator Drift Measurement Set-up °n built-in antennas tests for the effects
of downward modulation, and others.
The measurement of such characteristics is important, but a lack of standardized pro-
cedures precludes the possibility of discussion at this time.
BIBLIOGRAPHY
I.R.E. Standards on Radio Receivers, Latest issue. Methods of Testing F-M Receivers, 1947. Methods
of Testing A-M Receivers, 1948.
Foster, D. E., Receiver Characteristics, Communications, May 1939.
Characteristics of Broadcast Receivers, The R.M.A. Engineer, May 1940.
Matthews, A. C., Measurement of Receiver Characteristics, Radio, December 1944, March 1945.
Smith, F. Langford, Radiotron Designers' Handbook, Third Edition, Chapter 29, pp. 227-239.
Swinyard, W. <X, Measurement of Loop Antenna Receivers, Proc. I.R.E., Vol. 29, No. 7 (July 1941).
WAVE ANALYSIS
By E. Peterson
Some of the terms applied to devices which isolate, measure, and display the component
amplitudes of complex electric waves include wave, harmonic, and spectrum analyzers;
distortion and intermodulation meters and analyzers; and spectrographs.
28. WAVE CHARACTERISTICS
Waves to be analyzed may have components located at discrete frequencies or dis-
tributed more or less generally throughout frequency bands. Discrete components are en-
countered in studies of the response of a non-iinear circuit or circuit element to the action
of periodic waves. The resultant modulation products can be localized and measured
individually or, in some cases, collectively. Band distributions on the other hand are
found in speech and music and sometimes in noise. There, where the spectral distribution
changes with time, it is difficult to keep track of individual components, and measurements
are conveniently made of energies within bands of definite extent.
DISCRETE FREQUENCY DISTRIBUTIONS. Discrete or single frequency analysis
is used in a variety of fields such as noise reduction, machinery noise, power interference,
and modulation studies. Of these the last mentioned is the most important and the most
demanding. Modulation studies are of interest throughout the frequency range occupied
by the various communication services, and the amounts of power associated with them,
vary greatly in the different applications. Considering extreme cases, the power associated
with modulation products in long loaded cables and in multichannel carrier amplifiers may
be comparable with resistance noise in an audio band, while modulation products in high-
power radio transmitters may amount to kilowatts.
The frequency of any modulation product is expressible in terms of the fundamental
frequencies which produce it. If as example there are two fundamental frequencies A
and /i, the frequencies of all products are included within the expression \rnfi ± nfz\.
Here m and n are positive integers, or zero. Products may be distinguished by their
order, which is the sum of m and n. Thus the components 2/i, 2/2, |/i zh /a| are all of the
second order; 3/i, 3/2, \2fi =b /2|, ]/i =fc 2/2| are all of the third order.
WAVE CHARACTERISTICS 11-55
Modulation product amplitudes may be expressed in terms of the impressed waves or
fundamentals producing the modulation, or in terms of a significant component, using
arithmetic or logarithmic (decibel) scales for the ratios. Whereas in many detailed studies
each modulation product of importance is specified individually, in others, in which an
idea of the total modulation is required, the rms value of all unwanted products within a
certain frequency band is specified. Thus, in one method of testing distortion in a radio
link a sine-wave signal, preferably at a low audio frequency, is impressed upon the trans-
mitter. At the receiver output this component is removed by a filter or bridge type of
suppression network. The rms value of all remaining products in the audio band is
measured by means of a thermocouple or suitable rectifier. When expressed as a per-
centage of the rms fundamental in the normally terminated circuit, the ratio is termed the
distortion factor.
When the modulation of a particular circuit element is under consideration, and is to
be expressed in a way which would be applicable with the element connected in any given
circuit, it is customary to specify the equivalent (modulation) generator emf. This is
the voltage which, when inserted in the circuit made up of linear elements, gives rise to
the observed distortion products. It is used ordinarily of elements only slightly non-linear.
The ratios of modulation products to their fundamentals which analyzers' are used to
evaluate fall into two ranges of values. One applies to products falling within the frequency
range constituting quality impairment of the originating channel. The other characterizes
products which fall outside the transmitted frequency range, constituting interference
with other channels. Examples may be drawn from the audio, carrier, and radio broadcast
fields. Thus the requirements on a system transmitting speech are usually that the dis-
tortion products be at least 20 to 40 db down on the wanted components in the normal
channel ( 10 to 1 per cent in amplitude, or 1 to 0.01 per cent in power) . Interfering products
in other channels are restricted to smaller amplitudes. In multichannel carrier telephone
amplifiers the figures range from 40 to 80 db down ; in multichannel carrier grouping filters
which serve to separate transmitted and received currents the figures range from 70 to
120 db down. In certain radio transmitters the products appearing in other channels are
restricted to something of the order of 70 db down on the fundamentals. Corresponding
figures for elements or units which make up a system may be more stringent than those
specified for the system as a whole, especially where the modulations in several elements
or units contribute to the total.
TEST WAVES. In the analysis of speech, music, or noise, or of the output waves of
such devices as oscillators and harmonic producers, the questions involved are those of
isolating and measuring the components. In establishing the performance of circuits or
of circuit elements, however, the additional problem arises of specifying and of supplying
the wave to be used for test purposes.
Generally speaking, the input wave should permit an indication of the performance
of the apparatus to be tested, approximating as closely as possible the conditions of actual
use. Where the apparatus is subjected in use to an impressed wave of simple form, com-
paratively little difficulty arises since the wave can be readily reproduced by oscillators
and filter networks. On the other hand, the apparatus may be subjected to signal waves
which are highly complex in nature, such as those of speech. Such waves may require
comparatively elaborate and cumbersome setups for the measurement of modulation
products, especially where the fundamentals and the various products overlap in the fre-
quency spectrum.
To facilitate analysis, the complex signal waves are replaced by comparatively simple
ones. At the present time one of two types is ordinarily used according to the problem
encountered — a pure sine wave, or a complex wave consisting of two sine- wave components.
To prevent interaction of the two components before reaching the circuit under test, tuned
circuits, filter networks, or bridge networks may be employed. The amplitude of the
testing wave is chosen so as to traverse much the same region of the non-linear character-
istic as does the complex signal wave for which it is substituted. In some cases the test
wave is made to have the same rms value, and in others the same peak value, as the normal
signal. The test frequencies are so selected that, together with their important modulation
products, they fall in a frequency region of interest.
To illustrate the use of single- and two-frequency test waves consider the investigation
of a narrow band amplifier passing frequencies, let us say, from 100 to 110 kc. If a sine
wave of frequency 105 kc is impressed for test purposes then the harmonics are 210 kc,
315 kc, and so on, all harmonics falling outside the transmitted band and being greatly
attenuated. A measurement of distortion within the pass band would yield nothing. If,
on the other hand, instead of applying a single frequency, we impressed two frequencies
at 105 and 106 kc, say, the harmonics would fall outside the band and be attenuated as
before, but the third-order products at 104 and 107 kc would lie within the band, as indi-
11-56
ELECTRICAL MEASUREMENTS
cated in the spectrum (Fig. 1). These would furnish a useful indication of the non-linear
distortion which a single-frequency test wave could not provide. Another example may
be drawn from the same vacuum-tube amplifier. It may be shown that the amplitudes
of the above-mentioned third-order products depend upon the impedance offered to second
orders, one of which is the difference frequency (1 kc in the above example). This imped-
ance may vary widely in different designs without affecting the normal transmission or
n
|
0
Am
Ufier
I3
o
2/-3
'B
— n^,
Hrj
ana
/+/ ^
A^tLL-
o2
h/r/i
2/r
4^/a
•o
01
/i-
4-
-^/2
0 100 200 3UU
Frequency KG
FIG. 1. Output Wave Spectrum of Narrow-band Amplifier with Frequencies of 105 and 106 kc
Impressed
harmonic production. Figure 2 shows the results of measurement of third-order modula-
tion as a function of the frequency difference between the two input components. No indi-
cation of this significant effect would be revealed by a single-frequency testing wave.
Another instance in which the two-frequency test wave is used is in the measurement
of distortion produced by ferromagnetic-core coils. There only the main hysteresis loops
are called into play when a sinusoidal magnetizing force is applied, but with complex
waves of magnetizing force a different characteristic is involved since subsidiary loops
appear.
To exemplify the use of the single-frequency test wave, consider a vacuum-tube amplifier
supplied with power obtained from the 60-cycle line. There exists a certain amount of
modulation of each signal component with the 60 cycles and its harmonics in the amplifier.
To measure this effect a single-frequency test wave will serve.
BAND FREQUENCY DISTRIBUTIONS. Band frequency analysis involves measure-
ment of energies or amplitudes in the sub-bands into which the main band is divided. It
is usually employed for waves such as room noise or windage noise from certain types of
_^ machinery, which contain no promi-
nent discrete frequency components,
and for waves which contain discrete
frequency components varying rapidly
in both frequency and amplitude, such
as speech and music. Band frequency
analyses have also been used for waves
consisting largely of discrete frequency
components when it is unnecessary to
know the precise frequencies of the in-
dividual components. Examples come
up in studying the effect of vibration-
absorbing mountings and of the acous-
tical treatment of rooms for the reduc-
tion of machinery noise. In the com-
FIG. 2. Third Order Modulation at Amplifier Output munications field band frequency an-
Function of ^ the Two program materfal and of
Third Order db Down on Fundamenla
H* M U
o o o c
,
^
/
) 50 100 150 200
Difference Frequency
circuit noise are useful in determining
requirements to be placed on systems for reproduction of the input waves with the
desired fidelity and freedom from interference. For testing multichannel carrier systems,
the loading effect of many talkers has been simulated by introducing bands of resistance
29. GENERAL ANALYZER REQUIREMENTS
The requirements which an analyzer is called upon to satisfy in general are those ordi-
narily imposed upon any piece of measuring apparatus : that it furnish an indication of the
quantity sought, within certain limits of accuracy and of precision, without disturbing the
essential performance of the circuit to which it is applied.
GENERAL ANALYZER REQUIREMENTS
11-57
INPUT COUPLING. Connection of the analyzer to the circuit under test without
altering the essential circuit performance is accomplished by assigning a suitable impedance
to the input circuit of the analyzer. Three circuit arrangements have been used for this
purpose. These are the high-impedance or voltage-analyzer connection, the low-impedance
or current-analyzer connection, and the termination. In the first the analyzer is made to
have an impedance much higher than that of the circuit across which it is shunted. In
the second, the analyzer is made to have an impedance much smaller than that of the
circuit in series with which it is connected. In the third, the analyzer is made to have a
definite resistance to replace a resistance of the same value in the circuit studied. It will
be observed that, under these conditions, insertion of the analyzer will normally have
but little influence upon the normal functioning of the circuit studied, since all three may
be made balanced or unbalanced to ground as desired. Figure 3 shows connections to a
resonance type of analyzer as an example.
For current analysis, connection is made to
point a and for voltage analysis to point 6
when the resistor R is made large. For use as
a termination R is given a suitable fixed
value to fit the circuit or line to which it is
connected, usually 600 or 72 ohms. The re-
sistance r is usually made less than the effec-
tive resistance of the tuned circuit to avoid
reducing selectivity and may be adjusted
for the required gain.
A preferable connection for voltage analy-
sis, shown in Fig. 3b, usually permits a
greater fraction of the desired input voltage
component to be transmitted while main-
taining a high input impedance. Another
connection suitable for voltage analysis,
particularly useful over wide frequency
bands, employs a probe including a con-
denser-resistance divider (Fig. 3c). Its in-
put impedance is that of a 1- or 2-ju/if ca-
pacitance shunted by a resistance of the
order of 1 megohm. To make transmission flat with frequency, the two time constants
C\Ri and CzRz must be made equal.
RESOLUTION OF COMPONENTS. The analyzer band should be wide enough to
permit easy tuning-in of the desired component, including an allowance for variations in
frequency of the selected component. At the same time it must be narrow enough to
select a specific product. The equivalent band width of a selective circuit may be defined
as the band width of an idealized filter having a constant loss in the pass band equal to
the minimum loss of the circuit in question, infinite loss outside the pass band, and passing
the same amount of energy from a continuous constant-energy spectrum applied to the
input. Analyzers for the study of low-frequency machine noise require a band width from
3 to 5 cycles. Those for telephone circuit noise caused by induction from neighboring
power circuits require an equivalent band width of 20 to 30 cycles at least. For speech
and for general types of noise, band widths of 45 to 300 cycles are appropriate. For inter-
modulation studies of discrete components, the bands used range from a cycle or so at low
frequencies to several kilocycles and more at high frequencies.
Similarly the frequency discriminations required vary widely in different cases. In
fixed-band analyzers used for speech, discriminations of 20 db or so against components
located at the centers of neighboring bands are sufficient to provide useful information.
Other a-f analyzers usually require discriminations of the order of 25 to 50 db against
components 60 cycles from the tuned frequency.
The wide divergence in requirements has led to the development of a number of different
forms of analyzers, each suited to a limited class of work.
MEASUREMENT AND DISPLAY OF SELECTED COMPONENTS. With the
simpler manually operated forms of frequency analyzers, the point-by-point method of
analysis is employed. Here, for the discrete frequency analysis of a steady wave, the
frequency spectrum is explored point by point over the range of interest, and whenever a
component of importance is located its frequency and amplitude are observed. For band
frequency analysis of a periodic wave, measurements of the energy in each of a number of
adjacent sub-bands are made successively without reference to the distribution within the
sub-band. In analyzing waves of short duration which can be repeated a large number of
tunes during the exploration of the frequency spectrum, a similar procedure is followed.
FIG. 3, Analyzer Input Circuits Illustrating High-
input Impedance and Low-input Impedance Con-
nections
11-58 ELECTRICAL MEASUREMENTS
The net result of an analysis in which the several components are examined individually
is usually presented as a meter deflection. To permit the use of simple d-c meters the
selected wave feeds a thermocouple or a rectifier of the vacuum-tube or copper oxide type.
The thermocouple is somewhat sluggish in operation, and the process of tuning accordingly
must be slowed sufficiently to permit the products to produce an observable deflection.
The slow response is advantageous where the smoothing out of rapid fluctuations in the
selected wave is desired. Deflections are closely proportional to the square of the heater
current. This is a valuable property in estimating energies in band analysis. Tube and
varistor circuits may "be made much more rapid in operation and may be given a wide
range of desired relations between input amplitude and deflection by suitable choice^ of
operating potentials and circuit parameters. For high rectifying gain a small negative
bias may be used. For greater precision a large negative bias may be used since then a
small input change may be made to yield a large change in rectified output. By the same
token, however, an interfering component produces a correspondingly large change in
rectified output.
Where a graphical record of wave analysis is to be had in a short period of time, one of
several types of recording frequency analyzers is employed. These recording analyzers
are designed to perform automatically the same operations performed manually with the
simpler devices, including the plotting of wave component values. Recording analyzers
of this type may be used as well for the analysis of non-periodic waves of short duration
which san be repeated so that the effect of a steady wave is obtained.
Thus in the analysis of speech sounds and of single tones from musical instruments, or
of other non-steady waves which are not readily reproducible, with devices employing the
point-by-point method, the wave may be recorded and repeatedly reproduced. Finally,
non-steady waves may be analyzed directly without the necessity of recording them by
means of devices giving a visual indication of the complete energy spectrum of the wave
and capable of showing the rapid changes in spectrum which are characteristic of speech
sounds and some musical tones. A photograph of cathode-ray patterns or a recording on
electrically sensitive paper of the indications of such an analyzer can be made for a per-
manent record of the analysis. These arrangements are discussed in article 31, p. 11-65.
30. METHODS OF WAVE ANALYSIS
The earliest methods used for wave analysis were based upon observed wave forms —
observed directly by means of an oscillograph, or synthesized point by point from syn-
chronous contactor measurements. Wave components are deducible from the wave form
by application of Fourier series, which expresses the amplitude of any component as an
integral. Evaluation of the integrals is customarily handled by a time-consuming point-
by-point calculation, for which tables and schedules have been formulated to facilitate the
work. This method is useful when only harmonics of a single frequency are present in the
wave to be analyzed; when the wave has more than one fundamental, the computation
ordinarily becomes too involved to be useful, since a multiple Fourier series must be em-
ployed. For harmonics of a single frequency which are not too small in amplitude, the
accuracy of the determination depends largely upon the accuracy with which the oscillo-
gram is read, the number of points included in the analysis, and the order of the harmonic.
Because of its limitations, the computational method has been superseded by methods of
direct measurement, wherever possible.
The first direct method of analysis was that of Pupin, in which a series-resonant circuit
was used to select a component of interest, and amplitude was deduced from, the indication
of an electrostatic voltmeter connected across the condenser of the tuned circuit. Discrim-
ination by means of simple tuned circuits is employed in certain types of analyzers of the
present day, their sensitivity and flexibility being greatly increased by means of vacuum-
tube amplifiers. Selectivity and sensitivity are improved by having several tuned circuit
and amplifier units in cascade, and by substituting filter networks for the simple resonant
circuit. A different way to improve selectivity involves the use of a negative resistance
circuit to reduce tuned circuit losses.
RESONANCE ANALYZERS. Variable Timed Circuit. The simple form of current
analyzer shown in Fig. 4 is useful where a high degree of frequency selectivity is not re-
quired. It is made up of four units: coupling unit, frequency-discriminating network,
amplifier, and indicator. The tuning unit precedes the amplifier to discriminate against
other components of the input wave. This procedure reduces modulation in the amplifier,
which may introduce components of the same frequencies as those to be measured.
The tuning unit consists of a simple series-resonant circuit with the input wave intro-
duced through a small resistor. The amplifier input is taken across the condenser when
METHODS OF WAVE ANALYSIS
11-59
FIG. 4. Resonance Analyzer Circuit with Input
Arranged for Current Analysis t
the input fundamentals are of frequencies higher than the frequency of the component
being measured. When the fundamentals or other possible interfering components are at
Lower frequencies the amplifier input is connected across the coil for greater discrimination.
Ine amplifier is made responsive over the
frequency range of interest; it is usually of
the resistance-capacitance coupled type.
To increase the selectivity over that
available in the simple tuned circuit, several
discrirninator-amplifier units are used in
cascade. Efficient coupling between units
is provided by step-down transformers.
Here the signal level must be kept low-
enough to avoid appreciable modulation of
the fundamentals in the early amplifier
stages. A preferable arrangement from this
standpoint would be to locate as much of
the necessary frequency discrimination as
possible ahead of the amplifiers. For greater discrimination than simple tuned circuits
can conveniently afford, use is made of filter networks, which, being much more cumber-
some and less flexible in adjustment, are usually employed where only a small number of
fixed frequencies are to be measured.
The substitution method is currently used for evaluating component amplitudes since
the loss of the tuned circuit, and therefore
the analyzer response, varies with fre-
quency. The connections are shown in
Fig. 5, the switch being used to connect the
analyzer to either the test or the standard
circuits. The standard circuit includes an
oscillator adjustable in frequency, a vao-
FIG.O. Substitution-Method for Evaluating Com- umn-tube voltmeter or thermocouple and
ponent Amplitudes associated meter to indicate the standard
input, and a calibrated attenuator to vary
the input amplitude to the analyzer. The analyzer input impedance is fised at a value
at which the attenuator is properly terminated.
The test procedure consists in connecting the analyzer to the unknown, tuning in the
desired product, and adjusting the analyzer gain until a suitable deflection is obtained on
the output meter. The switch is then thrown to the standard side, and the standard
oscillator frequency is
varied until it coincides
with the analyzer tuning.
The attenuator is then
varied until the same de-
flection is obtained as be-
fore. The frequency of
the unknown component
may then be found from
the frequency calibration
of the standard oscillator
or of the analyzer, and
the amplitude is com-
puted from the voltmeter
reading and attenuator
setting.
Another form of reso-
nance analyzer with shunt
tuning in the plate circuits
of two amplifier
Ivolts across 600 Ohris M ,_, ,_
». 01 <ji ^ 03 <o o«-» h
1
814
—
i
z
3
2
I
°<
1
!
i
1 1
1 1
i
3 400 800
1200 1600 2000 2400 2800
FIG. 6.
Frequency: Cycles per Second
Spectrum of Noise on an Open-wire Telephone Circuit
has been used extensively
in the analysis of power-
frequency harmonics and
of induction from power
circuits. Voltages from 5 X 10 ~6 to 50 are measurable in the range up to 3 kc with an
accuracy of d=5 per cent. The discrimination of such an analyzer varies with frequency,
being about 40 db at 60 cycles from the tuned frequency when tuned to 180 cycles, and from
24 to 32 db 60 cycles away when tuned to 3000 cycles. Figure 6 gives an example of an
11-60
ELECTRICAL MEASUREMENTS
analysis of telephone-circuit noise caused by induction from power circuits. Approximately
1 hour is required to obtain with this apparatus the amount of data shown in the ngure.
The speed and ease of operation of the more modern analyzers have resulted in supplant-
ing the resonance type for all but special purposes.
Fixed Bands. A decidedly different form of analyzer using direct frequency selection
avoids the need for manual tuning to each frequency of interest by means of a bank of
fixed contiguous band-pass niters. Fourteen filters are used in one particular model to
Entire Spectrum
* i A L L
J O O O O O
Composr
Average 1
• Compcsit
Average T
j
e -
'ota
»-l
Fiv
I P
fhr
P
e Ma
ressu
ee Fe
ressu
e Voices
re =7.7 Bars
male Voices
e=6.3 Bars
ota
c -W
£ co
_-
— m
-.
_n
—
41
5 60
J-70
< -80
f-0
-100
-110
J
««L
r-
i ^ J j
—
-L
n
I
-
-
-
3456
8
1
10O
2
345681 2 345681
1000 10000
Frequency in Cycles per Second
FIG. 7. Average Speech Pressures per Frequency Interval of 1 cycle per second — normal conversational
voice. Distance 2".
cover the frequency range from SO to 12,000 cycles in approximately logarithmic steps.
The filters are connected in parallel at the input side and introduce a loss of about 8 db at
the crossover points and greater than 70 db over most of the frequency range beyond the
transmission band, A flux meter is used to integrate the sub-band output over a 15-second
interval for the measurement of average amplitudes, while a series of gas-filled discharge
tubes with associated relays and electrical counters measures peak magnitudes over a
54-db range in steps of 6 db. These measurements are made in one band at a time although
both average and peak measurements of the total spectrum may be made simultaneously
with the band measurements. Peak measurements in Vs-second intervals are made over
as long a time as desired. Figure 7 shows amplitude-frequency distributions for con-
versational speech for male and female voices.
Another type of fixed band analyzer has been used to measure distortion generated in
non-linear circuits by complex input waves. Here the input wave is made to pass through
a narrow band-elirnination filter before it enters the circuit to be tested. A narrower band-
pass filter is used for the analysis, with its pass band located within the band eliminated
at the input. By this procedure the band-pass filter output has had the fundamental
components eliminated, so that it constitutes a measure of distortion.
Feedback Type. A third means of providing frequency discrimination is particularly
useful for the analysis of discrete components in sub-audio- and audio-frequency ranges.
It consists of a negative feedback amplifier
TO incorporating a bridge type of network in
RECTIFIER its feedback path. One form shown in Fig.
8 uses a parallel T network made up of
capacitances and resistances which provides
high suppression at a single frequency. At
this frequency therefore the full amplifier
gain is effective. At frequencies removed
from the balance point, transmission
through the feedback network acts degener-
atively to reduce the amplifier gain. By
insertion in the feedback path, therefore,
the null of the network is transformed into a transmission maximum through the amplifier
circuit. The network null may be conveniently varied in frequency by ganging the three
resistors. Its selectivity remains constant on a percentage basis throughout the band,
independent of frequency.
Discrimination
METHODS OF WAVE ANALYSIS
11-61
The following figures on frequency discrimination apply to a two-stage amplifier with a
null set at 25 cycles. Roughly 12 per cent away from the null, the discrimination is 10 db;
20 per cent away it is 16 db, and in the limit approaches 45 db down on the maximum
transmission.
Transmission of the amplifier proper is made substantially fiat over the maximum range
of analysis. Beyond that, the gain and phase around the feedback loop are arranged to
avoid regeneration and oscillation, as in feedback amplifiers generally.
SUPPRESSION AND INTERMODTTLATION ANALYZERS. Although these two
analyzer forms are not related in general, it will be convenient here to take them together.
A simple type of suppression analyzer previously mentioned evaluates the rms sum of
the harmonics generated with usually a sinusoidal signal impressed. The fundamental
may be suppressed through the action of a resonant bridge, or a suppression filter, or a
twin-T network. The output includes any noise and interfering components which may
be present. If the harmonics are comparable in amplitude to these components, the
harmonic distortion proper cannot be found directly by this method.
Another form of suppression analyzer uses special procedures which are applicable to
the detection of a carrier and its two sidebands, as practiced in radio broadcast reception.
These procedures form the basis for a method of measuring intermodulation between two
frequencies in the audio band, one low (40 to 100~) and the other comparatively high
(1 to 12 kc) . The two tones are supplied to the system under test, and the output is filtered
to suppress the low-frequency tone. The residual wave is then treated as a carrier accom-
panied by the two sidebands to determine the extent to which the higher-frequency com-
ponent is modulated by the lower, as described below.
Measurement of Percentage Modulation. The special procedures referred to may
involve the cathode-ray oscillograph or the linear rectifier. If the modulating signal is
applied to the horizontal deflection plates of the oscillograph, and the r-f output consisting
of the carrier and its two
second-order side frequen- _^ ^ JL-
cies is applied to the vertical ^ ^ -----
deflection plates, then pat-
terns like those shown in
Figs. 9a and 95 are obtained
on the oscillograph screen,
according to the phase shifts
in the system. These pat-
terns yield the percentage
modulation from the lengths of the minimum and maximum ordinates indicated. One
hundred per cent modulation is obtained when the wave envelopes go to zero, and greater
modulations are indicated by intersection of the envelopes. When a linear sweep circuit
controlled by the modulating signal is connected to the horizontal deflection plates, rather
than the modulating signal itself, then Fig. 9c is obtained.
Knowledge of the percentage modulation permits the second-order sideband amplitude
(KP/2, in the figure) to be calculated accurately only when higher-order sidebands of the
carrier are negligibly small. In that event the envelopes of Figs. 9a, 97>, and 9c are respec-
tively linear, ellipsoidal, and sinusoidal. Otherwise the wave envelopes may be analyzed
to yield the amplitudes of the second- and higher-order sidebands.
Another method for determining percentage modulation, generally used to evaluate
intermodulation, employs a linear rectifier (envelope detector) to detect the modulated
carrier wave with a minimum of audio distortion. The percentage modulation is then given
as 100 times the ratio of the peak audio signal output to the d-c component. Where
higher-order products are present, they may be evaluated by resonance or heterodyne-
type analyzers.
HETERODYNE ANALYZERS. Dynamometer. Another method of analysis first
used by Descoudres employs a dynamometer, in which the unknown wave and a standard
wave of known frequency, amplitude, and phase are respectively connected to the two
coils of the dynamometer. Since the dynamometer deflection is proportional to the product
of the currents in the two coils, a constant deflection is obtained when the frequency of
the sinusoidal standard is made equal to that of a component of the unknown wave. The
magnitude and phase of the component are then found from a calibration when the stand-
ard phase is adjusted for maximum deflection. To determine the magnitude without
regard to phase, the standard frequency is offset by a fraction of a cycle from that of the
component under measurement, and the maximum swing is observed. The method is
limited to comparatively low-frequency work.
From one standpoint the dynamometer may be regarded as fulfilling three functions:
modulating the unknown with the standard wave, filtering the beat frequency output, and
(a)
Time
a?) ro
FIG. 9. Modulated Wave Patterns
11-62
ELECTRICAL MEASUREMENTS
indicating the amplitude of the difference frequency component. Improvement in fre-
quency response and in sensitivity has been obtained by replacing the dynamometer by a
vacuum-tube modulator, and further increase in sensitivity is obtained again by amplifying
the beat frequency output. As an indication of the component to be measured, use may
be made of either the lower sideband or the upper sideband formed by the beating oscillator
and the component under investigation. To select this product, mechanical, electrical, or
piezoelectric niters and networks are conveniently located in the frequency range. These
replacements of the functions discharged by the dynamometer result in the most widely
used of all analyzers, the modern heterodyne type.
A particularly simple form of heterodyne analyzer has been adapted to the measurement
of products not too small in relative and absolute amplitudes. In this arrangement no
amplifier is used, and the mechanical movement of a meter connected in the plate circuit
of a modulator tube serves to provide frequency discrimination as it does in the dynamom-
eter.
General Tube Modulator Type. The heterodyne analyzer possesses a number of advan-
tages over other types which have brought it into wide use. To mention the outstanding
ones, first of all it uses a fixed discriminating circuit which is readily made highly selective
and stable, and takes up little space- Next, the tuning-in of a desired band requires but a
single adjustment — the frequency of the heterodyning oscillator. Finally the response can
be made fiat over an extended frequency range so that the substitution method of evaluat-
ing amplitudes is not required. Relative levels can be taken directly as the difference
between attenuator settings.
Essential units of a representative model are shown in the schematic of Fig. 10. The
principal elements comprise coupling unit, modulator, beating oscillator, filter, amplifier,
and indicator.
COUPLING HETERODYNE MODULATOR SELECTIVE
OSCILLATOR NETWORK
FIG. 10. Heterodyne Analyzer Circuit
The coupling unit is shown unbalanced to ground with a calibrated attenuator which
serves to vary the input to the modulator. The analyzer therefore is used as a termination,
but other coupling units for voltage or current analysis can be fitted to the input terminals
of the attenuator.
The modulator is of the conjugate input type, to provide a convenient means for sepa-
rating the signal and beat frequency circuits, to balance out the beat frequency oscillator
wave in the output circuit, and to reduce the number of unwanted modulation components
produced. Triodes have been used with the grid bias set close to plate-current cut-off.
The shielded and balanced input coil shown should have uniform transmission over the
frequency range of interest, and its modulation should be well below the amplitudes of
the products measured. By the usual design procedure, the response of the modulator
can be made uniform over a wide range of frequencies.
With values for noise, band width, and modulation which are readily attained, analyzers
have been constructed capable of measuring second-order products 80 db down and third-
order products 100 db down on their fundamentals. Here a three-stage amplifier was
used with a gain of 130 db. The net analyzer gain including losses in the modulator and
band filter was 120 db.
Where products larger in relation to their accompanying fundamentals are to be meas-
ured, the amplifier gain may be reduced. Where products smaller in relation to their
fundamentals are to be measured, it becomes necessary to insert added discrimination
METHODS OF WAVE ANALYSIS
11-63
against the fundamentals in the input to the modulator, so that we arrive at a combination
of resonance and heterodyne types.
The osciUator used for heterodyning is designed to have a high degree of frequency and
amplitude stability with supply voltage and temperature variations, and with 'time.
Harmonics in the output are generally kept more than 40 db down on the fundamental.
The oscillator amplitude applied to the modulator is made much greater than the signal
input and slightly smaller than the grid bias, so that grid current does not flow in the
modulator tubes. This amplitude, moreover, should be maintained fairly constant over
the frequency range. All these requirements can be met readily with a bridge-type oscil-
lator using thermistor or varistor stabilization. Frequency variation is most easily effected
when the oscillator itself is of the heterodyne type, but frequency stability is not as high
and spurious products have to be guarded against.
The ability of the analyzer to discriminate against neighboring input components is
determined largely by the properties of the modulator tubes and by the selectivity of the
selective network of Fig. 10, which may be made up of
electromechanical, electrical, or piezoelectric elements.
Which of these is used is a matter of convenience and of
the frequency at which the band is to be located. Quartz
crystals are generally used from 40 ke up to several mega-
cycles. The band width is made narrow to cut down the
noise introduced by the modulator to the greatest possible
extent, as well as to reduce unwanted components. On
the other hand, the band width should not be made so
small that the tuning-in of the desired products becomes
unnecessarily difficult and time-consuming. An equiva-
lent band width of 5 to 20 cycles is found to be a useful
compromise between the two requirements, the greater
band width being used for measurements at radio broad-
cast frequencies. Analysis of waves in the short-wave
region requires wider bands to accommodate incidental
frequency variations; 2000-cycle bands have been used.
The frequency at which the band is located depends upon
the location of the frequency spectrum to be analyzed.
In order to avoid confusion of the measured compo-
nents with extraneous products generated in the modu-
lator, the band is placed either above or below the spec-
trum to be analyzed. Thus, in analyzers designed for use
at carrier or radio frequencies, the band may be set at a
low frequency; frequencies ranging from a fraction of a
cycle to 1000 cycles have been used in various types. To
avoid ambiguity in the measurement of small power-
supply ripples or modulation products, the band should
be made narrow and offset from harmonics of the power
frequency. In an analyzer covering the range from 50 kc
to 6 Me, the crystal filter is located at 6.7 Me and has a n nemueiiuy, iw ^uca. jj,
band width of 400 cycles. In audio analyzers the beat piezoelectric network, midband 50
,. - n i j i_ j.t u j 1 1 i -A kc. C, resonant circuit (Q = 100)
frequency is generally placed above the band; 11 kc, ou tuned to 1 kc.
kc, and 90 kc have been used. Figure 11 shows the fre-
quency discrimination obtainable in several different types of selective circuits. The
100-cycle network referred to in that figure is a cumbersome multisection affair weighing
close to 100 Ib.
Since the amplifier is required to function over only the narrow band passed by the
selective filter, it is conveniently built with screen-grid tubes or pentodes and tuned inter-
stage coupling which permit of realizing comparatively high gains per stage. The tuned
interstage coupling supplements the selectivity of the band filter and limits the noise
output of the amplifier. An input transformer with a high step-up ratio may be used to
minimize the effect of tube noise arising in the first amplifier stage.
Machine Noise Analyzer Unit; Mechanical Band-pass Filter. This device is used over
the range from about 30 to 5000 cycles. It employs a mechanical band-pass filter working
at 6000 cycles and having an equivalent band width of about 25 cycles. The effect of a
double-balanced modulator is obtained in the electromagnetic structure through which
the driving force is applied to the filter. In covering the above frequency range, the
frequency of the heterodyning oscillator is varied from 6000 to 11,000 cycles. A discrimi-
nation of about 48 db 60 cycles from the tuned frequency is obtained in the four-section
mechanical filter. The analyzer unit does not contain input or measuring circuits since
band
10 20 30 40 50 50
Cycles from NCdband
11. Frequency Discrimina-
A, electrical network, mid-
frequency, 100 cycles. B,
11-64
ELECTRICAL MEASUREMENTS
it is intended to be used in conjunction with a noise meter which furnishes these circuits.
It is readily portable. Fig-
ure 12 gives an example of
the noise spectrum of a
small synchronous motor
obtained with this ana-
lyzer.
General-purpose Ana-
lyzer Unit with Piezoelec-
tric Band-pass Filters.
With this device, it is pos-
sible to select either a 27-
cycle band or 200-cycle
band, from any part of the
frequency range between
30 and 1 1 ,000 cycles. Lat-
tice-type quartz crystal fil-
ters working at 50 kc are
employed for both hands.
For the narrow band, a dis-
crimination of 52 db 60 cy-
cles from the center of the
DU
55
^50
CO
§45
i«>
^35
Iso
,0
•S3
25
20
) 200 400 600 800 100O 1200 1400 1600 180020002200 24C
frequency irt Cycles per Second
FIG. 12.
Noise Analysis of Small Synchronous Motor — 1/4 hp, 1800
rpm, 60 cycle, three phase, 220 volts, no load
band is obtained, while the wide band has a similar value 350 cycles from midband. The
circuit includes a demodulator by means of which the wave components selected by the fil-
ter are translated to their original frequencies
as indicated in the schematic of Fig. 13. This
^* arrangement is particularly valuable in mea-
suring closely spaced products, since it avoids
output indication produced by transmission
of the heterodyne source itself through modu-
FIG. 13. Heterodyne Analyzer Circuit Used for lator unbalance (carrier leak). The modula-
Frequency Selection. The modulator-demodu- tor leak here is translated to zero frequency
JMSS&7S: Sffi383£Z££ ^d so is not transmitted by the a-c system
connected to the demodulator output. The
demodulator leak is far removed in frequency from the selected component and can be
made harmless. Both modulator and demodulator are of the double-balanced copper oxide
J.UU
90
080
or
05
<5
570
I
"t 60
O3
§
JD
o50
**S
40
30
(
J^
•^
1
-L-^__
-U^L.
V
fifh no So
Fan a
ind Insulat
id Exhaust
on on
\_
" L.
\
r-r
-r~U
I
lr
Fan and E
sulated fo
haust — *
Noise
V
I-,
-u-^
_J— —
^
-L^
*-I-^_
"-u^
> 1000 2000 3000 4000 5000 6000 7000 8000 9000 10,000
Frequency - Cycles per Second
FIGL 14. Band-frequency Analysis of Exhaust Fan Noise
SPECTROGRAPHS
11-65
type and are supplied with carrier heterodyning power from the same oscillator through
buffer^ amplifier stages. The analyzer unit does not include input or measuring circuits
S1??VVS mtended as an attachment for a noise meter or similar measuring device of
which these circuits are a necessary part. Figure 14 gives an example of the use of the
200-cycle band in the analysis of exhaust fan noise to determine the noise reduction ob-
tained at various frequencies by means of sound insulation on the fan and exhaust.
31. SPECTROGRAPHS
Investigation of the spectrum of a complex wave by the methods just presented is a
comparatively slow process at best since manual adjustment of a resonance frequency or
of a beating oscillator frequency is required to shift the analyzer from point to point along
the band to be studied. To speed up the process the analyzer may be tuned automatically,
and the spectral distribution displayed in its entirety.
RECORDING TUNED CIRCUIT ANALYZER. Here the resonant frequency of a single
electrical tuned circuit is varied in small steps over the frequencj- range by means of a
player-piano pneumatic control. Simultaneously a photographic record is made of the
current in the resonant circuit after amplification and rectification, the photographic paper
being correspondingly stepped in position to accord with the frequency scale. Two fre-
quency ranges are provided: 20-1250 cycles and SO-5000 cycles. The complete recording
takes about 5 minutes. A 20-db amplitude range is the useful limit for a single record,
the amplitude scale on the photographic record being approximately linear. Discrimina-
tion in the 80-5000 cycle band is about 20 db 60 cycles away from the tuning frequency,
decreasing somewhat when the tuning frequency is above 1000 cycles. Figure 15 presents
100
400 600 100O» 2000
Fro. 15. Record of 160-cycle Buzzer Output
300O 5000
the analysis of a buzzer tone, each peak of the curve denoting the amplitude and frequency
of an input component.
In any scheme of this kind which shifts a single discriminating circuit over the bandT a
definite compromise has to be made between the speed at which the circuit is shifted and
the consequent resolving power, or ability to separate neighboring components. This
relationship is discussed quantitatively below in the discussion of the Sweep Frequency
Heterodyne.
TUNED-REED ANALYZER. This analyzer makes use of a series of eleetromagnetically
driven reeds tuned to frequencies in the audio range, distributed with a uniform percentage
difference in frequency. Each reed carries a small concave mirror which deflects a beam
of light by an amount proportional to the oscillation amplitude of the reed. The vibrating
Cycles per Second
400
800
1600
3200
Piano Tone
Piano Tone F
FIG. 16. Frequency Spectra Obtained with Reed Analyzer
spots of light indicate on a ground-glass screen the components present in the input wave
which is applied to the electromagnets driving the reeds. Damping of the reeds is pro-
portional to frequency and provides a discrimination of 20 db for components 2 1/2 per cent
from the tuned frequency. A component 20 db down on the maximum can be evaluated
11-66
ELECTRICAL MEASUREMENTS
with an accuracy of about 1 db when its frequency coincides with that of one of the reeds.
A permanent record of a spectrum distribution constant in time can be obtained photo-
graphically. To record wave components varying with time a motion-picture camera must
be used. Figure 16 shows spectrograms for two piano tones obtained with a demonstration
analyzer of this type, covering the frequency range from 50 to 3200 cycles with 144 reeds.
COMMUTATED BAND ANALYZER. Selection of components is effected by a bank
of contiguous fixed band niters extending over the frequency range to be covered. The
output of each band filter is rectified, filtered, and amplified, as shown in Fig. 17. The ver-
tically deflecting (V) plates of a cathode-ray tube are connected to each channel m turn
by means of a commutator, while the horizontally deflecting (H) plates are connected to a
synchronously operated stepped sweep. In this way, a linear frequency scale is laid out
along a horizontal axis on the cathode-ray screen, and a vertical line represents the wave
amplitude or energy within the corresponding band filter. The general aspect of spectro-
grams of this type is indicated on the oscilloscope screen depicted in the figure.
FIG. 17. Commutated Band Analyzer; Cathode-ray Presentation
From 10 to 30 filters have been used with band widths distributed linearly or logarithmi-
cally to cover the audio spectrum. With the linear distribution, bandwidths of 300 to 150
cycles have been used. Filter attenuations at the crossovers are 3 to 6 db, and at the mid-
band frequencies of the immediately adjacent niters are of the order of 20 db. A non-
linear compressor inserted in the lead to the vertically deflecting (T7) plates of the cathode-
ray tube helps to make the smaller amplitudes more readily perceptible. Accurate por-
trayal of an extended amplitude range, however, requires increase in filter selectivity to
reduce interference from components falling within the attenuating regions of the filters.
Commutation should be fast enough to reveal any envelope variations transmitted by the
band filters. Thus if the widest filter band of the bank is B cycles wide, variations at a
rate of B/2 are freely transmitted. The rectifier low-pass filter therefore should be B/2
cycles wide, or a little wider. For faithful indication, then, each channel should be sampled
B times per second at least. While mechanical commutators have been shown for sim-
plicity in Fig. 17, the channel sampling commutator may be replaced by electronic means,
including clamps and a ring, with as many stages as there are bands to sample. Similarly
the sweep commutator may be replaced by a properly synchronized electronic sweep
developing a sawtoothed wave form.
SWEEP FREQUENCY HETERODYNE, CATHODE-RAY PRESENTATION. This
method uses what is essentially an automatic heterodyne analyzer and is in general use
throughout the radio frequency spectrum, from the broadcast band and below, to the
centimeter region. A block diagram of the circuit arrangement is shown in Fig. IS. There
a sweep generator provides a sawtooth wave at a sub-audio repetition rate for two purposes.
First, it constitutes the horizontal sweep, and second, it provides a means for varying the
beating oscillator frequency throughout a definite frequency range. To accomplish the
second function, the sawtooth wave actuates a reactance tube associated with the fre-
quency-determining circuit of the oscillator. Or, at ultra-high frequencies, the sawtooth
wave is impressed directly upon an oscillator tube of the velocity- variation type. In
either case, the oscillator frequency is made linearly proportional to the instantaneous
amplitude of the sweep throughout its utilized portion.
The variable oscillator output then modulates the input wave to be analyzed so as to
sweep its spectrum across the narrow pass band of the i-f amplifier. The i-f output is
tiien detected, amplified, and applied to the V plates of a cathode-ray oscilloscope.
SPECTBOGKAPHS
11-67
Sweep-frequency Heterodyne Analyzer; Cathode-ray Pres-
entation
The amount of frequency variation (F) during a sweep cycle is made large enough to
include the region to be analyzed. The sweep period (T) and the i-f band width (B) must
be selected to accord with the resolving power required. If, for example, components equal
in magnitude and separated by S cycles are to be displayed as distinct pips on the oscillo-
scope screen, the response produced by one of them must have built up and decayed to a
sufficiently low value before the next component enters the i-f band. The transient
response depends upon the i-f band width and has a duration of roughly %/B seconds. This
time is to be no greater
than the time required for
the sweep to traverse the
frequency spacing between
the two components, or
ST/F. If then the i-f
bandwidth is made, say,
one-quarter the frequency
separation between the
components to be resolved,
the sweep period T should
be of the order of magni-
tude F/2£2. Where the FlG- 18*
components to be resolved
are not equal in magnitude, the sweep period or the sweep frequency deviation must ^ be
correspondingly reduced, if the two transients are not to overlap excessively. Resolution
of a carrier and two sidebands is indicated on the oscilloscope screen of Fig. 18.^
In certain cases involving large numbers of components, it is desirable to display the
envelope of the spectral distribution rather than to resolve the components individually.
There the i-f band (B} is made wide enough to include a number of components, and the
approximate relations given above remain applicable when the separation (S) refers to
bands rather than to individual components. An example is shown in Fig. 19 of a spectrum
envelope applying to a magnetron pulsed at 1SOO cps, taken with an i-f band width of the
order of 50 kc. •
Various applications involve ranges of T from 1/100 to perhaps 1/2 second, of # from
2 to 100 kc, and of F from 100 kc to 200 Me.
One of the most satisfactory methods for calibrating the frequency scale is to superpose
on the modulator input of Fig. IS a standard frequency source which is amplitude modu-
lated by a sine wave at a known and adjustable rate.
This superposes three pips at known frequencies ^on
the signal spectrum, which can be varied in position
to coincide with points of interest.
For presentation of individual components a linear
rectifier may be used to provide a linear output scale.
For envelopes a square-law rectifier provides an out-
put proportional to energy. Measurement of output
levels may be carried out by one of two methods.
The deflections may be read on a calibrated scale on
the cathode-ray screen, or a calibrated attenuator in
either input or i-f paths may be varied to bring to a
fixed deflection the particular part of the distribution
which is to be evaluated. In either method, over-
loading of the measuring system must be avoided.
A similar sweep type of heterodyne analyzer, de-
veloped primarily for the study of musical tones, has
a galvanometer as output indicator A rotating
mirror synchronized with the 10-cycle oscillator fre-
quency sweep reflects the galvanometer light spot to
a ground-glass screen. The rotating mirror thus pro-
vides the equivalent of a horizontal sweep. An
electrical network is used at 20 kc with a band width sufficient to resolve tones separated
YAnother indicating and recording device used in conjunction with the sweep frequency
heterodyne was developed primarily for noise and vibration studies in the audio band It
uses a scriber provided with a synchronous mechanical drive (like that of Fig 20) which
furnishes a permanent record of the spectral distribution upon waxed paper Piezo niters
make available analyzer band widths of 5, 50, and 200 cycles. The amplitude scale covers
a range of 80 db. A complete record, directly legible, requires about 2 minutes time.
7 me
FIG. 19. Spectrogram of an Oscillating
Magnetron Pulsed at 1800—; Pulse
Duration Roughly 0.25 Microsecond.
Wave components are not resolved.
11-68
ELECTRICAL MEASUREMENTS
SOUND SPECTROGRAPH. The sound spectrograph produces a visual record show-
ing the distribution of energy within an audio band in both frequency and time. Though
the development of this device must be regarded as still in the experimental stage, it con-
stitutes as it stands a powerful means for the analysis of speech, music, and noise. Its
power comes from the high concentration of information presented, which permits details
of the spectral distribution to be followed as a function of time. _
Figure 20 shows a simplified schematic of one form of the device which will serve to
illustrate the basic idea. Three distinct functions are involved. First the sound to be
analyzed is recorded so that it can be repeatedly reproduced. Here a magnetic tape
recording is shown, mounted on a rotating disk which is driven by a synchronous motor.
Second, analysis of the recorded sound is effected by a heterodyne type of analyzer in
which the oscillator frequency is varied to move the analyzer filter in effect steadily over
the sound spectrum. This variation is indicated in the figure by mechanical coupling
between the varying condenser of the beating oscillator and the main drive shaft. In
this way the analyzing frequency changes a small amount throughout each revolution of
the shaft. Finally the analyzer output is recorded in synchronism with the ^reproduced
sound. Recording is accomplished in the same manner as that practiced in facsimile
reception. A drum bearing
the recording paper is coupled
to the main drive shaft, and
the recording stylus is moved
laterally a small distance in
each revolution by means of a
lead screw similarly coupled.
The electrically sensitive paper '
mounted on the drum is
marked by the stylus with
gradations of density which
accord with the analyzer out-
put. The net result is to pro-
duce a sort of
sional picture
three-dimen-
which the
FIG. 20. Schematic Representation of One Form of Sound Spec- energy distribution is depicted
trograph. The output of the sweep-frequency heterodyne ana- v d it variations on a
lyzer is displayed as a pattern on electrically sensitive paper, ex- "J •* . ,
hibiting the energy-frequency distribution as a function of time, rectangular plot of frequency
against time.
A signal level range of 35 db is handled with the aid of automatic volume control which
provides something like a threefold compression on a db basis. Two heterodyne band
widths are available: one 45 and the other 300 cycles, as measured at the 3-db points. The
linear frequency scale of the spectrogram is 2 in. high and covers the range from 100 bo
3500 cycles. The linear time scale extends for a length of 12 in., corresponding to an
original audio sample 2.4 seconds in duration. Two hundred rotations of the disk carrying
the audio sample are completed in less than 5 minutes for the full analysis. The most
recent development in this field speeds up the analysis by a factor of the order of 200.
Photographic reproductions of spectrograms of speech, music, and noise are to be found
in the last four references listed under Spectrographs in the Bibliography. In the case of
speech, the narrow band (45 cycles) analysis is adequate to resolve individual harmonics
of the voiced sounds. The traces curve up and down as the pitch of the voice varies, and
the spacing between harmonics gets bigger as the pitch increases at any particular instant.
A definite loss of detail occurs when the wide baud (300 cycles) is used since two or three
harmonies are merged. A spectrogram of thermal noise shows energy concentrated in
different frequency regions at different instants of time. Randomly spaced vertical spin-
dles of the spectrogram correspond in length to the 300-cycle filter of the analyzer. Espe-
cially interesting are spectrograms of a warble tone which constitutes a frequency-modu-
lated wave, produced by varying sinusoidally the frequency of an oscillator. The narrow
filter reveals the presence of individual side frequencies of a tone warbled at a 50-cycle
rate, but the wide filter cannot resolve them; they are integrated to reveal the instantaneous
frequency.
The process of sound portrayal employed in the sound spectrograph described above
results in a considerable simplification of apparatus where high resolution is desired. The
equivalent machine to record high-resolution patterns directly would require something
of the order of a hundred filters rather than a single one. Sound spectrographs of this type
have been made to transcribe long samples of sound by employing the disk and drum
arrangement of Fig. 20 with endless belts, one of magnetic tape and another of recording
paper.
MICROWAVE MEASUREMENTS 11-69
For special uses, such as experimental visual telephony for the deaf, low resolution pat-
terns of the type provided by the sound Spectrograph are formed at speech rates. Ten to
twenty fixed filters or a scanning band affording equivalent resolution are used in this
instrument, termed "visible speech translator." The outputs produce speech patterns in
light upon a moving band of either phosphorescent or fluorescent material. Scanning
and timing functions are controlled by synchronized electronic means. The accuracy and
speed of these translators are sufficient to permit their use for the reading of continuous
speech by trained observers.
BIBLIOGRAPHY
Resonance Analyzers
^^^ ^^BAyrf^n?lectrical ^ave Analyzers for Power and Telephone Systems, Trans. AJ.B.B.,
Vol. 48, Il\j7 (1929).
Sivian, Dunn, and White, Absolute Amplitudes and Spectra of Certain Musical Instruments and
Orchestras, J. Acous. Soc. Am., Vol. 2, 330 (1931).
Scott, Analyzer for Sub-audible Frequencies, /. Acous. Soc. Am., VoL 13, 360 (1942).
Suppression and Intennodulatfon Analyzers
Wolff, A-c Bridge as a Harmonic Analyzer, J. Optical Soc. Am.t VoL 15, 163 (1927).
•q^p FV Sc°2 e' Analysis and Measurement of Distortion in Variable Density Recording, J.
Billiard, Distortion Tests by the Intel-modulation Method, Proc. I.R.B., VoL 29, 614 (1941).
Hayes, A New Type of Practical Distortion Meter, Proc. I.R.E., Vol. 31, 112 (1943).
Pickering, Measuring Audio Intel-modulation, Electronic Industries, June 1946.
Warren and Hewlett, Analysis of the Intel-modulation Method of Distortion Analysis, Proc. I.R.E.,
Vol. 36, No. 4, p. 457.
Heterodyne Analyzers
Vol. 18, No. 1, 178 (1930).
Arguimbau, Wave Analysis, Gen. Radio Experimenter, VoL 8, Nos. 1 and 2, 12 (1932),
Castner, A General Purpose Frequency Analyzer, Bdl Labs. Rec., VoL 13, 267 (1935).
Spectrographs
Wegel and Moore, An Electrical Frequency Analyzer, Bell Sys. Tech. J., VoL 3, 299 (1924).
Potter, Transmission Characteristics of a Short Wave Telephone Circuit, Proc. I.R.E., VoL 18, 583
(1930).
Hickman, An Acoustic Spectrometer, J". Acous. Soc. Am., VoL 6, 108 (1934).
Wolf and Sette, Some Applications of Modern Acoustic Apparatus, J. Acous. Soc. Am., VoL 6, 160
(1935).
Schuck, The Sound Prism, Proc. I.R.E., VoL 22, 1293 (1939) ; Panoramic Reception, Electronics, VoL
14, 36 (1941); Recording Sound Analyzer, Electronics, VoL 16, 100 (July 1943).
Williams, R.F. Spectrum Analyzers, Proc. I.R.E., January 1946.
Gaffney, A Spectrum Analyzer for Microwave Pulsed Oscillators, Waves and Electrons^ Vol. 1, 83 (1946).
Apker, Kahnke, Taft, and Watters, Wide Range Double Heterodyne Spectrum Analyzers, Proc. I.R.B.,
1947.
Montgomery, Techniques of Microwave Measurements, Rad. Lab. Series VoL 11, Chapter 7, McGraw-
Hill.
Koenig, Dunn, and Lacy, The Sound Spectrograph; Riesz and Schott, Cathode Ray Translator;
Dudley and Gruenz, Visible Speech Translators with External Phosphors, J. Acous. Soc. Am.,
July 1946.
Potter, Kopp, and Green, Visible Speech, Van Nostrand, 1946.
Kersta, Amplitude Cross-section Representation with the Sound Spectrograph, J. Acous. Soc. Am.,
November 1948.
Mathes, Norwine, and Davis, The Cathode Ray Sound Spectroscope. J. Acous. Soc. Am., September
1949.
General Surveys
Bourne, Wave Analysis, Electronic Eng.t VoL 15, 149, 281, 472; VoL 16, 31 (1942); 3, bibliography.
Scott, Measurement of Audio Distortion, Communications, VoL 26, No. 4, 23 (1946).
MICROWAVE MEASUREMENTS
By E. W. Houghton
The electrical characteristics of any network can be completely expressed in terms of
three quantities: impedance, power, and frequency. Attenuation ratio, although not a
fundamental quantity, is of sufficient importance to warrant separate consideration. This
section is concerned with methods and techniques for accurately measuring these quan-
tities in the frequency range of roughly 1000-30,000 megacycles. The methods can be
used to attain the accuracies summarized in Table 1.
11-70
ELECTRICAL MEASUREMENTS
Table 1. Microwave Measurement Accuracies
Quantity to Be Measured
Method
Accuracy
Impedance:
Slotted line
±2%
Directional coupler
Hybrid junction
Slotted line
±5% - ±0.2%
±5% - ±0.2%
±5%
Power (averaged over several seconds)
5-200 microwatts
Bolometer
±0.5db
02 10 milliwatts
Bolometer
±0.1 db
00 1-1 00 watts
Bolometer-attenuator
±0.3db
20- 1 00 watts
Calorimeter
±0.3db
Power (averaged over several microseconds)
1- 1 00 watts
Calibrated crystal
±0.6 db
0 1—100 kilowatts
Calibrated crystal
±1 db
Attenuation
0-3 db
Bolometer
±0.05db
0- 1 3 db
Bolometer
±0.1 db
0_60 db
Heterodyne receiver
±0.2db
0-40 db .
R-f attenuator
±0.2db
Frequency:
Small differentials . .-•
Wavemeter
, ±0.005%
Absolute
Harmonic generator
±0,0001%
Wavemeter
±0.01%
32. IMPEDANCE MEASUREMENTS
TRANSMISSION-LINE CALCULATIONS. At microwave frequencies practically all
measurable impedances are in transmission lines (coaxial or wave guide) , and the terminals
of these impedances are transmission-line couplings (i.e., coaxial jacks and plugs or wave-
guide cboke or plane flanges) or simply specific transverse planes in the transmission line
(see reference 17, p. 11-89). Absolute impedance values are rarely important, and in
fact wave-guide transmission-line impedances can be denned in several ways (see refer-
ence 1). Ambiguity is removed by using a relative or "normalized" value which is the
ratio of an impedance, 2, to ZQ, the characteristic impedance of the transmission line defined
in the same way; thus z = Z/Z^ where z is a complex value.
A section of uniform, lossless, transmission line, Fig. 1, transmits energy in a given
mode between a source plane, s-s, and an impedance plane, t-t, by means of traveling
electromagnetic waves. Unless the impedance at t-t termi-
nates the line in its characteristic impedance, two such waves
exist: (1) an incident wave which originates at the source and
travels forward toward the impedance plane t-t, and (2) a
reflected wave which originates at t-t and travels backward
toward the source (see reference 2). The ratio of transverse
voltage in the reflected wave to transverse voltage in the
incident wave defines the reflection coefficient k, which is a
complex quantity. Total transverse voltage and longitudinal
current on the transmission line are the vector sums of the
voltages and currents in the two oppositely traveling waves, which therefore combine to
produce a standing-wave pattern distributed along the transmission line. The ratio of
the maximum to the minimum total voltage defines (voltage) standing-wave ratio, S,
which is not a complex quantity.
The more general result of interference between oppositely traveling waves is to trans-
form the impedance at t-t to new values at planes between s-s and t-L The relationship
between reflection coefficient and normalized impedance at t-^t is : Kt \4> = (zt — l)/(z< + 1),
where zt is a complex value. At some arbitrary plane a-a closer to the source and removed
from t-t by line length l/\g wavelengths the reflection coefficient is ka = Kt \<j> — 20,
where & - 2?rZ/Xg radians. The normalized impedance at this plane is thus:
1 -f
9 Incident
jvave
o b <
j
i t
1
I
1
t
!
Reflected
s wave <
, !
; b <
1 "
1 *
FIG, 1. Impedance Planes on
a Transmission. Line
This car* be expressed as &* = (st + j tan #)/(! -+- jzt tan fl).
The oppositely traveling waves combine in phase opposition to give a minimum voltage
IMPEDANCE MEASUREMENTS
11-71
standing wave at 2<r « (» - <£) radians, or (TT - £)/47r wavelengths from «; at */2
radians or 1/4 wavelength closer to s-s the waves directly add to give a maximum voltage
standing wave. The standing-wave ratio is thus 8 = (1 + j£*)/(l — Kt}. From measure-
ments of either K, or S, and o-, the normalized impedance at t-4 can be computed (see
reference 3) from
1 -
^ The transmission-line calculator (see reference 4), Fig. 2, provides a convenient graphical
aid to visualization and computation of the above impedance transformations. An ex-
Pi Q. 2. Transmission Line Calculator
ample, drawn on the chart, will illustrate its use. As the line length between t-t and a-a
increases, transformed impedance values are intercepted by the circle in the order indicated
by the arrow on its periphery. Thus a normalized impedance zt = Q.do -f- j'0.45 at t-t
transforms to za — 1.5 -f ;0.7 at plane a-a located 0.102 wavelength from i-i. Normalized
admittance values equivalent to series impedance values appear at points on the circle
diametrically opposite; thus ya = 1/Za = 0.55 — J0.25. At b-b, zt is transformed to a
pure resistance Zb — 2.0 + j"0; at c-c, zt is transformed to zc = 0.5 + ^"0, also a pure resist-
ance. Planes 6— b and c~c are the positions of the maximum and minimum standing wave
voltages respectively, and the standing-wave ratio created by 2* is S = 25 = l/z« = 2.
Following the above example in reverse order it is seen that the chart provides an ex-
tremely practical method for computing the impedance zt from measurements which- gave
values of 5 - 2 and <r = 0.408. By this method eq. (1) can be solved rapidly and with a
precision adequate for most measurements.
The results of impedance measurements are primarily used to study the electrical nature
of the impedance, or to design networks for transforming this impedance to a new value
11-72 ELECTRICAL MEASUREMENTS
(see reference 5) (usually the characteristic impedance of the transmission line, which it
then terminates without reflection). However, in many cases a given impedance may be
used to terminate an electrically long transmission line or a line of unspecified length.
Under these conditions a measurement of the reflection coefficient phase angle would be
trivial; thus in many practical cases impedance measurements are concerned only with
ascertaining reflection coefficient amplitudes or standing-wave ratios produced by that
impedance in a connected transmission line.
STANDING- WAVE DETECTORS. Of the three instruments most commonly used
for impedance measurement the standing-wave detector is the most versatile since it
affords information on both amplitude and phase of the reflection coefficient. It comprises :
(1) a section of uniform transmission line (coaxial or wave-guide) which has a longitudinal
slot in its outer conductor, and (2) a probe which projects through this slot and travels
parallel to the axis of the line on a carriage. A standing-wave pattern of voltage is set up
in the line when the test impedance is connected at one end and a source at the other.
The probe, excited by this voltage, is connected to a detector whose output is a relative
function of total voltage amplitudes along the slotted line. From readings obtained at
the maximum and minimum voltage positions, the standing-wave ratio can be calculated,
provided that the law of the detector is known or the detector has been calibrated. The
detector may be a crystal (reference 6), bolometer (reference 8), or the mixer of a hetero-
dyne receiver (reference 25). In the last case the mixer may be kept linear by operating
at low levels; the second detector is used at a constant level by means of a calibrated i-f
attenuator. The law of a bolometer detector and its bridge circuit can be obtained accu-
rately by a low-frequency calibration. Specially selected crystals can be found to meet a
square-law requirement over restricted input ranges, but they should preferably be cali-
brated against a bolometer power meter or heterodyne receiver.
A somewhat less accurate calibration method is to terminate the slotted line in a per-
fectly reflecting short and measure the standing-wave voltage distribution, which under
ideal conditions approaches V = Csin (2irl/\g), where C is a constant and l/\g is the
displacement in wavelengths from a plane of zero voltage. A method for which the law
need not be. known is to operate the detector at a constant level by using a calibrated r-f
attenuator between the slotted line and the source, or between the pick-up probe and the
detector; standing-wave ratios are deduced from attenuator settings. The r-f attenuator
method is satisfactory for measurement of high standing-wave ratios (10-100) but is
generally considered inferior to other methods for low ratios (1 to 2) .
In order to avoid reflection errors from the probe, its insertion is limited to small values
(less than 10 per cent of wave-guide height or */4 the difference between coaxial conductor
diameters) for which its power output will be 20-30 db lower than the power in the slotted
line. The most convenient oscillator sources are single-cavity klystron (reference 10) or
Reflex (reference 8) oscillators which can be easily tuned over wide bands. After adequate
padding these sources may deliver only 1-10 mw to the slotted line. High-sensitivity
detecting and indicating methods are therefore often required. Three methods are
•common: (1) a heterodyne receiver can be used; (2) a simpler method is to 100 per cent
modulate the source by a square wave (to avoid frequency modulation), then amplify
and rectify the detector output in a high-gain amplifier-detector; (3) the simplest method
is to use a sensitive galvanometer or microammeter driven directly by a crystal detector.
A tunable transformer can be included in the probe-detector mechanism to give the high-
est sensitivity allowed by a given probe insertion; however, any variation in crystal or
bolometer r-f impedance with standing-wave voltage variation may cause a change in the
tuning and introduce a significant error. Since they are 15-20 db less sensitive than crys-
tals, bolometer detectors are more satisfactory on high-power sources (magnetron test
equipment, reference 11) for which high-sensitivity methods are not needed. For ac-
curate measurements, stabilized power supplies must be employed, and spurious pick-up
in microwave oscillators, high-gam amplifiers, and detector output leads must be avoided
by complete shielding.
Design Requirements. The slot should be as narrow as possible, of uniform width,
accurately centered in rectangular wave guide and parallel to the axis in the coaxial line,
and long enough to allow a probe movement of at least 1/2 wavelength. To prevent radia-
tion the slot can be covered (by a contacting shoe or a shorting trap) for at least 1/4 wave-
length on each side of the probe. To avoid serious errors caused by small transverse varia-
tions of the probe in the slot the probe's outer conductor is sometimes imbedded in the
•center of a metal slug at least i/2 wavelength long, the bottom of which is flush with the
anside of the outer conductor or wave-guide wall, and the sides of which definitely wipe (or
definitely dear with very small gaps) the sides of the slot. In coaxial slotted lines the con-
ductors must be accurately coaxial. The center conductor can be rigidly supported and
oentered at the source end, but at the load end it should be supported (if necessary) by a
IMPEDANCE MEASUREMENTS 11-73
very thin washer of low-dielectric-constant material; the residual reflection (pure shunt
susceptance) can be calibrated and allowed for subsequently. An assortment of low-reflec-
itL ^ T^f"8' JaCkS' Plug8' ada*>ters> may ^ required for connection to the load,
although greatest accuracy can be attained with as few attachments as possible. Wave-
guide slotted hnes are preferably terminated with a well-surfaced plane flange, to which
adapters may be attached, or with a standard choke on one end and choke-cover flange on
the other so that either type of connection is available by reversal of the slotted section.
Ihe most serious requirement is that the bottom of the probe shall travel accurately
parallel to the axis of the transmission line. The probe carriage may travel on the outside
of the line itself, or on ways rigidly attached and made accurately parallel with the axis.
It is generally possible by accurate machining or electroforming techniques (reference 12)
to maintain parallelism within ±0.0002 in. for at least i/2 wavelength of travel.
^ Accuracy. On standing-wave ratios above about 2, inaccurate assumptions (or calibra-
tions) for the law of the detector and the amplifying-indicating system, and meter-reading
errors, can easily limit the measurement accuracy to 10 per cent; by using a calibrated
r-f attenuator, or preferably a heterodyne receiver, or by deducing the voltage standing-
wave ratio from measurements confined to the region of the voltage minimum (reference
3) , the accuracy can be improved to nearly that for low standing-wave ratios. Below ratios
of 2, percentage accuracy is limited primarily by: (1) change in characteristic impedance
and end reflections introduced by the slot; (2) reflections introduced by load connectors
(flanges, jacks, tapers, or adapters) , unless these are to be considered a part of the unknown
impedance; (3) reflections from the probe; and (4) non-parallelism of probe' travel. The
effect of (1) can be deduced by measuring an impedance through two Hnes of the same
dimensions, one with and the other without a slot. Sometimes errors from (2) can be
reduced by determining an equivalent shunt susceptance (reference 16), but this is im-
practical when the connector introduces multiple discontinuities. It is possible, but not
very easy, to measure and calculate errors from (3) (reference 13); this effect can be
reduced by maintaming a matched impedance looking toward the source and eliminated
by withdrawing the probe until there is no significant change in power delivered to the
load (as monitored by another detector); but a compromise must usually be effected
between this error and the error from (4) since (4) is reduced by larger probe insertions.
Experience has shown that carefully constructed coaxial standing-wave detectors can
be used with an accuracy of about 5 per cent and the accuracy for wave-guide detectors is
usually about 2 per cent.
DIRECTIONAL COUPLERS. Directional couplers (reference 14) are commonly in-
cluded as a permanent section of the coaxial or wave-guide transmission line in microwave
systems for monitoring incident and reflected power (reference 15) . In such applications
they (1) introduce negligible reflection in the transmission line (S less than 1.05), (2) create
almost no high-power arcing problem, and (3) contain no moving parts. Compared to
standing-wave detectors, directional couplers can be used for routine measurements of re-
flections with somewhat less accuracy by standard techniques, and with much higher ac-
curacy by special techniques; they can be more conveniently used (1) to tune a load impe-
dance to match the line, (2) to tune a source impedance to match the line, and (3) to cor-
rect for changes in interaction loss between the source and load impedance.
Power levels proportional to the power in the reflected and incident waves can be meas-
ured at the input and output ends respectively of an auxiliary transmission line coupled
to the main line by means of two equal-sized probes, loops, or orifices separated by approxi-
mately 1/4 transmission-line wavelength (reference 14). Illustrated in Fig. 3, this instru-
ment comprises a directional coupler in its simplest form. A directional coupler can thus
be used to measure reflection-coefficient
amplitude, which is the ratio of the square
root of the two measured power levels, source i is^^t ~^r~7~
Bolometer power detectors are convenient I .,^ *a*t^I^'u m^i-^
for high-power sources, and on low-power
sources the same sensitive detecting and | | " AwdBary fe»«
indicating methods previously described R|^|d
are applicable. It is preferable to switch wave output
the same detector-indicator alternately be- jr^ 3 Directional Coupler in Waveguide
tween incident and reflected wave outputs
(alternately terminating the other output) so that only a ratio calibration is required.
Low-reflection wave-guide and coaxial switches are convenient for this purpose, or special
arrangements can be employed to transmit both waves to the same output. Detector
law uncertainties can be eliminated by using a calibrated r-f attenuator to equalize incident
and reflected powers. The attenuator method is best used for measuring nearly matched
impedances, since, for example, a change in standing-wave ratio from 1.01 to 1.02 changes
11-74
ELECTRICAL MEASUREMENTS
Oscillator
Attenuator
-
Tunable
matching
network
I t
3
I
Y Snorting
piston
A. Tuning source impedance
to match tne transmission line
I i
1
_deal
ource
Source
^*&mmWb^
s
' \^ l $fa
Adjustable
attenuator
n
Detector
and
Indicator
B, Simulation of perfectly stable, matched source
the reflected wave output power by 6 db whereas one from 2.02 to 2.04 changes the output
power by only 0.12 db. . . , ,
A directional coupler can thus be used as a sensitive indicator for tuning a load to match
the transmission line, and, because reflection coefficient is continuously monitored, it is
especially convenient. , .. .
In Fig. 4 a directional coupler is used for matching a source impedance to the line. As a
shorting piston (or preferably a reflector with a constant K of 30 to 50 per cent) is moved
back and forth in the line, the tuning controls are adjusted until the incident wave output
remains constant. The oscillator must be sufficiently masked or decoupled to prevent
changes in its frequency and
efficiency as the load impedance
• varies.
Without tuning for it, the
condition prevailing for a
matched source impedance
(Fig. 7) can be simulated by
monitoring and keeping the in-
cident power constant by means
of a variable attenuator ahead
of the coupler, Fig. 4. The
variation of power in the load
as its impedance changes is re-
duced to that of reflection loss
only. Power-time instability in
the oscillator can also be cor-
rected for by this method.
Design Requirements. Di-
rectional couplers for imped-
ance measurement should not
have losses much below 20 db
(see p. 11-72) to avoid serious
loading by the coupling holes
and interaction between them.
By careful machining or electro-
forming techniques (reference
12), inside dimensions and the
wall thickness of the main line
must be made precisely uniform
over the longitudinal region oc-
cupied by the coupling slits or
holes, which must be con-
structed with exacting tolerances. Transverse slits have been used both in coaxial lines
and in wave guides (usually in the wide side), but for wave-guide couplers round holes in
the narrow side are usually better since they give higher losses which can be more accurately
controlled by standard precision boring techniques. In coaxial lines the center conductor
must be accurately centered; reflection from any support at the load end cannot be cali-
brated out of the measurements which ordinarily do not contain phase information. Simi-
larly, careful attention must be given to designing refleetionless fittings and connectors.
The most serious requirement for accurate measurements is that the directional coupler
be designed for the frequency band in which it is to be used. Its directional coupling
action (directivity) is frequency sensitive. As Xg, the transmission-line wavelength (not
to be confused with free-space wavelength) varies, the effect of a fixed hole spacing is to
add a spurious vector voltage to the true reflected wave output in the auxiliary line. The
ratio of this spurious voltage to the incident wave voltage (also in the auxiliary line) shall
be designated "unbalance reflection coefficient," Ku. In the worst case, a measured value
of reflection coefficient will be in error by ±KU. For a simple two-hole coupler in wave
guide, Ku is zero at a Xg approximately 1 per cent greater than four times the hole spacing,
but for a ±0.6 per cent, ±1.3 per cent, and ±3.2 per cent change in Xg the values for Ku
are approximately 0.01, 0.02, and 0.05 respectively. The band width can be greatly
increased by increasing the total number of holes, and the simplest pattern is to separate
equal-sized pairs of holes (spaced 1/4 the mid-wavelength) by 1/2 mid-wavelength. By
this method Ku can be kept lower than 0.015 over an 8 per cent wavelength band in a four-
hole wave-guide coupler and over a 20 per cent band for an eight-hole wave-guide coupler
(reference 26).
C. Precision measurement of
reflection coefficient
FIG. 4. Directional Coupler Applications
IMPEDANCE MEASUREMENTS
11-75
•anch
H branch
>L Hybrid junction in waveguide
Another spurious vector, adding to the true reflected wave output, comes from partial
reflection of the incident wave from an imperfect termination of the auxiliary line. Where
it is practical to position this termination for first a minimum then a maximum reading, it
is possible to nearly eliminate its error by averaging the two readings.
Accuracy. In the laboratory where there is usually no serious limitation on length,
it is practical to use four- or eight-hole couplers containing broad-band terminations with
VSWR less than 1.05 in coaxial and 1.02 in wave guide. Under these conditions, routine
measurements can be made with a VSWR accuracy of about 10 per cent in coaxial and
5 per cent in wave guide, since detecting-indicating systems can be made to contribute
small percentage errors. In microwave systems directional couplers are often limited in
size so that the realizable accuracy is usually lower.
Figure 4 shows a method wherein the auxiliary line termination is tuned to cancel the
Ku of the holes, giving the effect of a perfect coupler and termination. As a mismatch of
constant K is moved back and forth in the main line, the termination tuning is adjusted
until the reflected wave output remains constant (not zero) . Alternatively, if a termination
of K — 0 is used the output can be directly tuned to zero. Loads (including their con-
nectors) connected to the directional coupler can then be measured with an accuracy of
about 0.1 to 0.2 per cent. Accuracy is limited primarily by the detecting-indicating
equipment.
HYBRID JUNCTIONS. Hybrid junctions (reference 18) can be used in many of the
applications described for directional couplers, compared to which they may possess certain
advantages in sensitivity, size, design simplicity, and
band width. It is possible to make hybrid junctions
in either wave-guide or coaxial lines. However, a de-
sign which will give accurate measurements over a
wide bandwidth does not yet exist for coaxial lines.
Descriptions and examples in the following discussion
are applied specifically to wave-guide hybrid junctions
for which satisfactory designs are commonplace.
A type of hybrid junction commonly used for imped-
ance measurement is formed by joining an J?-plane T
(off the narrow side) and an ^-plane T (off the wide
side) to a straight section of rectangular wave guide
(reference 12) . Projections of the central axes of both
T's meet at a common point on the axis of the main
guide, Fig. 5. This geometrical symmetry makes the
E and H branches conjugate. When the main
branches are terminated by equal impedances there is
no transmission between E and H branches. Hybrid
junctions can therefore be used to tune a load on one
main branch (test branch) to match that on the other
main branch (reference branch) ; the degree to which,
the tuned load matches the characteristic impedance
of the wave guide depends upon (1) the intrinsic bal-
ance in the junction and (2) the reflection coefficient
of the reference termination. The directional coupler
has corresponding limitations; in fact, both devices
separate out direct and reflected waves by a cancella-
tion process. However, it is sometimes more helpful to visualize the hybrid junction as
the microwave equivalent of a low-frequency hybrid transformer (reference 18) with the
added complication that the input impedances at the junctions, unless matched, are
transformed to new values along the transmission-line branches.
Looking toward the junction the impedances are inherently unmatched to the branch
transmission lines; on well-constructed junctions the VSWR's looking alternately into
E, H, test, and references branches are approximately 2, 3, 1.3, and 1.3 respectively when
the other three branch lines are terminated in ZQ.
By methods similar to those described for the directional coupler, hybrid junctions can
also be used for routine and precise measurements of reflection coefficient. Figure 5
illustrates the circuit configuration. The ^-branch output (detector input) is proportional
to the vector sum of the reflected waves in the test and reference branches, and a wave
created by junction unbalance. When the latter two are negligible, the detector input is
proportional only to the power reflected from the unknown impedance; reflection coefficient
can be deduced from the ratio of this power to the power incident upon the unknown. For
sensitivity calibration a power level proportional to the incident wave (in the test branch)
B. Measurement of reflection coefficient
FIG. 5. Hybrid Junction
11-76 ELECTRICAL MEASUREMENTS
is most conveniently applied to the detector by substituting a shorting plunger for the
unknown. . 7 a , ,
As a consequence of its reflection coefficient, kt, the test branch carries a total reflected
wave, Vr, which is not uniquely proportional to the product of the reference incident wave
Vi and the unknown reflection coefficient kx. In fact, Vr = Vikx/(l - kxkt), which is a
complex quantity. Evidently the amplitude ratio VT/Vi as measured on the hybrid
junction is not the true reflection coeflicient Kx\ therefore the maximum error in routine
measurements created by Kt (assuming that the effect is not canceled by purposely
phasing the unknown along the line) is 1/(1 - K*Kt). For example, a measurement
which gave Kx = 9.1 per cent (SWR = 1.2) may be in error by a maximum factor of 1.01
since Kt = 13 per cent. The error increases at higher values of Kx, but nearer zero the
error from this source will be negligible (reference 27) .
When a short circuit is substituted for the unknown for sensitivity calibration, Kx = 1.
As tbe position of the short circuit is varied the power in the detector will deviate from the
reference value by maximum factors of 1/(1 4- Kt) to 1/(1 - Kt}. From an observation
of the maximum and minimum detector outputs it is possible to deduce that reference
detector output which is proportional to the reference incident power in the test branch,
However, the impedance presented to the source will be seriously altered by the short
circuit in the test branch, so the above factors can be applied exactly only when the oscil-
lator is well masked and the source impedance is well matched to the line; alternatively
the source's incident power can be monitored by a directional coupler and kept constant,
Fig. 4. The detector must also present a well-matched, ZQ, load. An alternative method of
calibration which reduces the interaction effects occasioned by introducing a shorting
piston is to substitute a known impedance (calibrated by other means) of medium or
low K. In this case, the net measurement accuracy can be no better than that of the
calibrated impedance.
The above interaction effects can be materially reduced or even eliminated by introduc-
ing properly positioned susceptances (references 5 and 17) (matching posts, windows, or
dielectric blocks) which cancel the junction's discontinuity reactances and transform the
impedance of the H and E branches so that each branch is matched when the other three
are terminated with matched loads. Under this condition, the main branches are also
conjugate, and power sent into any one branch divides equally between the two non-
conjugate branches (reference IS). Such an "ideal" hybrid junction can be used in all
those applications described for directional couplers, except monitor, without disturbing
the transmission line, with as good accuracy and higher sensitivity. For example, high-
er low-impedance mismatches can be measured accurately, a load can be tuned, and
a source impedance can be tuned to ZQ by monitoring and tuning for constancy the
incident wave output on one main branch while moving a shorting piston in the other main
branch.
The above impedances may be matched over only a relatively narrow band, unless the
posts or windows are put right in the junction. However, the unbalance reflection coeffi-
cient may be seriously increased by this method of impedance matching. Completely
satisfactory wide-band solutions have not yet been found. Matching networks are not
essential for many measurement requirements.
Accuracy. Accuracy of routine measurements is primarily limited by (1) interaction
between unknown and test branch impedances, (2) reflection coefficient of the reference
termination, and (3) junction unbalance reflection coefficient. For low mismatches (K
less than 5 per cent) the first error is negligible, and under this condition the same tech-
niques described for directional couplers can be used to (a) cancel the second error by
positioning the reference termination and (6) cancel both second and third errors by
timing the reference terminations for precision measurements. On hybrid junctions
constructed by precision electroforming techniques (reference 12) the unbalance reflection
coefficient can be kept less than 0.005 over the entire wave-guide pass band. Therefore
on low mismatches the accuracy of routine measurements can be as high as or higher than
on well-constructed directional couplers with the added advantage that lower-sensitivity,
more stable detecting and indicating equipment can be used.
Compared to directional couplers, hybrid junctions have the following advantages:
(1) they are simpler to design for a low unbalance reflection coefficient over a wide band
(geometrical symmetry is the only requirement); (2) they are smaller; and (3) they are
more sensitive (the reflected wave power in the detector is at least 10 db higher than that
for a 20-db directional coupler) . However, (1) they cannot be incorporated in transmission
lines (with negligible reaction) to monitor reflection coefficient; (2) interaction between
"unknown" and test branch impedances may introduce a significant error in measuring
reflection coefficients higher than about 5 per cent (S = 1.1) ; and (3) impedance interaction
effects make it more difficult to calibrate sensitivity without introducing a calibration error.
ABSOLUTE POWER MEASUREMENTS
11-77
33. ABSOLUTE POWER MEASUREMENTS
Brrdge circuit
connection
Quarterwa
stub supp
R-f input
Dielectric-
; r^ bypass
\ T
r
Thermistor bead
•obe aoienna
. la waveguide
R-f Input
TWVOT l +^ T n on BY ^OLOMETRIC METHODS. Microwave
powers less than 10-20 mw are measured by bolometric methods which are, so far, the
only ones available for accurate measurements in this frequency and power range. A
transmission line carrying the unknown power
is terminated in a bolometer detector, the only
absorbing element of which is a thermally sensi-
tive resistor. Its d-c resistance changes when
r-f power is dissipated in it, and ideally the
change is independent of the frequency of exci-
tation. The resistance change can therefore be
related to r-f power by a low-frequency or d-c
calibration. Alternatively the resistance can R-f «nj
be biased to a given value and kept constant
when r-f power is applied by removing an equal
and measured quantity of d-c or low-frequency
power.
A bolometer detector (Fig. 6 is typical)
comprises a thermal resistor and a reactance
network for matching it to the transmission
line. Sensitive thermal resistors are small,
essentially "lumped," elements. Two types
are commonly employed: thin, short, filament
wires (reference 19), and bead thermistors,
the thermal element of which is a tiny bead
made up of a mixture of metallic oxides (ref-
erence 8) (see Table 2). The r-f resistance
of the thermal resistor may be different from
d-c resistance, but, in order to compare r-f
power directly against d-c (or low-frequency)
standards, (1) its d-c resistance change must
be dependent only upon incremental heating
power (when external temperature is constant),
(2) the heat distribution from r-f power must
be equivalent to that generated by a uni-
formly distributed d-c current, and (3) all
the r-f power absorbed by the detector must be
dissipated in the thermal resistor.
Requirement 1 is met on all thermal resistors when space-integrated values of resistance
and heat are specified. However, the time constant of the thermal resistor may be of
such a value that, in two extreme cases, resistance changes either (a) exactly follow or
(6) completely fail to follow the modulation envelope of the r-f power (when amplitude
modulated) . In either case the average resistance change is proportional to average power,
but in (a) envelope peak power can be measured- As sinusoidal modulation frequency is
increased from zero (all other parameters remaining constant) the resistance modulation
will decrease to half its maximum value at 36 cps and at 450 cps, respectively, for the ther-
mistors and platinum wire listed in Table 2.
Table 2. Sensitive Thermal Resistors — Typical Characteristics
Dielectric
r-f bypass
I?. In coaxial
FIG. 6. Pre-tuned, Wide-band Bolometer De-
tectors
Platinum Wire
Thermistor Bead
Temperature
25° C
200 ohms
15.3mw
+4.5 ohms/mw
— 0.0 5mw/deg cent
350 Atsec
11 ma
0.118 X 0.00006 in.
25° C
200 ohms
10 mw
— 29 ohms/mw
Lead'
Bead,
25° C
125 ohms
I3.5mw
— 1 4 ohms/mw
— 0.1 mw/deg ce
2500 fjsec
200 ma
wares, 0.001 in. d
0.020 X 0.0 10 in
25° C
50 ohms
23.5 mw
— 4.8 ohms/mw
at
iameter
t.
Resistance . ...
Resistance-power coefficient . .
Power-temperature coeffi-
cient *
Time constant "f
Safe rnaxiTTiuTn ciirrpnt - -
Dimensions
Tor constant resistance; also the ratio of power to temperature changes which produce the same
resistance changes.
f For 67 per cent of ultimate resistance change.
11-78
ELECTRICAL MEASUREMENTS
SJS 0.2
£ =
Source VSWR>
Requirement 2 is met on filament wires by (a) designing a matching configuration which
places the r-f current maximum at the midpoint of the wire, and (6) by limiting the upper
frequency to that corresponding to a free-space wavelength of about 8 times the length
of the wire (reference 7). Platinum wires have given satisfactory results up to 10,000
megacycles. Bead thermistors, which are more nearly ideal "lumped" elements, have
been used up to 25,000 megacycles, where they have shown discrepancies less than 5 per
cent when checked against calo-
0-6 { ' ' ' ' ' ' ' ' rimeter standards.
Requirement 3 must be met by
transforming the a-c resistance
component to the transmission
line's characteristic impedance
with a matching network in which
considerable care is taken to elimi-
nate extraneous circuit losses from
sliding contacts, joints, and con-
ductors. This problem is simpli-
fied by (a) biasing the thermal re-
sistor to a reasonable resistance
(50-200 ohms) and by (6) design-
ing a low-Q matching configura-
tion, which tends to eliminate high
current concentrations (standing
waves) in the detector.
The power absorbed (and there-
fore measured) by a detector load
is a function of both source and
load impedances, and, depending
upon relative phase angles (or line
length), varies between the limits
shown in Fig. 7 (reference 20). To
eliminate these uncertainties in
measurement and interpretation of
power quantities it is evidently de-
sirable to use a detector that pre-
sents a nearly matched impedance.
Wide-band, pretuned detectors, in
addition to being especially con-
venient to use, inherently meet the
low-£ requirement. Table 3 lists
the band widths that have been
realized for typical pretuned bo-
lometer detectors using thermi-
stors.
Since the r-f impedance varies with it, the thermal resistor's d-c resistance must be
kept nearly constant by varying (with temperature) the biasing power by methods peculiar
to the bridge measuring circuit.
Table 3. Bandwidth-Impedance Characteristics of Typical Pretuned Thermistor
Detectors
-0.6
For the above VSWRs, line lengths are chosen so that
Pj = least power and Pnt=most power in the load.
Available power Ffc could be delivered if conjugate
impedence- matching transformers were used in the line.
FIG. 7. Power Delivered by a Mismatched Source to a Mis-
matched Load
Frequency Band
in Megacycles
Maximum
VSWR
Transmission Line
Thermistor Operating
Resistance in Ohms
5 to 600 .
2
Coaxial
Ch ' f 7 f r
700 to 1500
4
Coaxial
100
2900 ± 17 2%
4
inn
3700 ±8.1%
4
Coaxial
inn
4500 ±111%
4
1 T^
4100 ± 12.2%
2
oaxia
7c
4600 ±8.2%
1 l
2 in. X I in. OD
7r
9.050 ±6.1%
I 4
2 in. X 1 in. OD
1 'JC
24,0€0 ± 4.2%
1 4
1 1/4 in. X 5/8 in. OD
1/2 in. X 1/4 in. OD
ABSOLUTE POWER MEASUREMENTS
11-79
MTHiammeter
'Microammeier
Biasing and power-indicating circuits are designed to accom-
as those shown in Table 2. Resistance changes are most
f • , -,- . i - - ~ ge c*rcufts such as Fig. S which illustrates the simplest method
°* }hlrdiff^S f8?? ?°Wel a ud measuring ^ P^er. Power can be directly measured
as the difference of the two d-c biasing powers required for reference resistance, one before
d^dva^l r'f P°wer ls fPPHed. However, this simple method contains three important
disadvantages. (1) since the r-f power may be a small difference of two relatively large
d-c powers, small meter-reading errors may introduce
large errors in the difference power measurement; (2)
r-f power is not continuously indicated; (3) the unbal-
ance caused by external temperature changes subse-
quent to initial balance conditions are indistinguishable /> ^_TA_IX Bolometer
from r-f power changes. <L X^ZL, /deiSs
Difference errors, (1) , can be reduced by interposing a T X>— -3 * JjJS"1
resistance network between the bridge and a current or ^ e e
voltage source which is kept constant at a precisely mea- Fl<J' 8' B^^^S™** f°r
surable single value. The network must contain accu- Bolometer Detectors
rately known resistance elements, one or more of which are switched in or out in small and
™^ni?tepS< Biasing Powers are then deduced from settings on the switch.
Within the accuracy limitations imposed by (3), unbalance current can be used as a
continuous indication of relative r-f power level; absolute power can be deduced from a
calibration of the unbalance sensitivity. This sensitivity calibration will be an uncritical
but not negligible function of temperature unless the d-c voltage across the bridge can
be kept constant (this can be made possible by using variable low-frequency biasing power
to balance the bridge initially) . Resistance unbalance must be limited to a maximum value
dictated by the detector's r-f matching requirements.
The^lowest power that can be accurately measured is limited by (3) and the temperature
coefficient of the thermal resistor. For example, from Table 2, a subsequent temperature
change as small as ±0.1 deg cent would cause a 3-db error in measuring powers of 2.5-5 juw
and 0.1 db in measuring powers of 0.25-0.5 mw. These errors can be materially reduced
by (a) using^thermal insulation, (6) using large metal masses to limit the rate of temperature
change, (c) interposing between the source and the detector an essentially instantly oper-
able cut-out switch, reactive gate, or attenuator which can then be used to remove r-f
power rapidly to check the initial balance, and (d) using temperature-compensating
bridges. A combination of all the above techniques is usually required for accurate power
measurements in the range of 5-100 /iw.
A practical solution to the disadvantages of the simple bridge circuit has been to com-
bine all the remedies into a more complex circuit such as Fig. 9. The thermal resistor in,
Calibrating
circuits
Regulating \\ Bridge-regulated
bridge \\ osoiLaior
Compensating-^
thermal resistor
k— R-f input
Measuring
therm aJ resistor
FIG. 9.
Temperature-compensating, Self-calibrating, Direct-reading Bridge Circuit for Bolometer
Detectors
the bolometer detector is used as the regulating element in a conventional bridge-regulated
oscillator. The oscillator automatically delivers enough power to the thermal resistor to
bias its resistance very close to the bridge-balancing value (within 1 per cent). The oscilla-
tion power level will therefore vary with ambient temperature with a coefficient determined
by the temperature coefficient of the thermal resistor. From Table 2, this coefficient
would be —0.05 mw/deg cent for the platinum wire and —0.1 mw/deg cent for bead
thermistors.
The output of the low-frequency oscillator is also delivered to another bridge which
contains a compensating and measuring thermal resistor (never excited by r-f power) of
11-80 ELECTRICAL MEASUREMENTS
the same type as that used in the bolometer detector. When RI is properly adjusted the
power received by the compensating resistor varies with temperature at a rate equal to
that required by this resistor to be biased to a constant resistance. Both thermal resistors
must be subjected to identical external temperature variations. Intimate thermal cou-
pling can best be accomplished by burying the compensating thermal resistor in the
same metal mass (preferably large) which forms the outside boundaries of the bolometer
detector.
As a net result the measuring bridge remains balanced, even though temperature
changes, until r-f or incremental d-c power is applied to the bolometer detector. The d-c
biasing powers are kept constant so that the unbalance sensitivity of the measuring bridge
does not vary with temperature. The overall sensitivity is established at one power level
by using the d-c calibrating network which introduces a known increment of d-c heating
power in the bolometer detector. Other unbalance current readings can be related to the
calibrated point from a knowledge of the indicator law. Both the measuring bridge net-
work and the intrinsic characteristics of its thermal resistor influence the law of unbalance
current versus power input. In general, this law is not exactly linear, but it can be accu-
rately calibrated by exciting the detector with a convenient low-frequency source whose
relative output power is varied in known ratios by a low-frequency attenuator.
Accuracy. It is usually practical to limit errors from r-f sources to very low values,
and then power-measurement accuracy is primarily governed by the d-c calibrating and
indicating circuits. The circuit of Fig. 9 can be used to measure full-scale powers with
less than ±0.1 db error, half-scale powers within ±0.2 db, and quarter-scale powers within
±0.3 db. On an indicating meter whose resistance is equal to the bridge arms, deflections
of 200 and 50 microamperes per milliwatt are typical for thermistors and platinum wires
respectively. Therefore powers below 1/4 mw cannot be very accurately measured unless
meter-reading errors are kept low by using sensitive galvanometers or very stable indicator
amplifiers; it is then possible to attain accuracies of ±0.4 to 0,6 db down to 5-10 juw.
However, the severe temperature drift problems must be solved by exacting methods as
discussed above.
MEDIUM AND HIGH-POWER MEASUREMENTS BY BOLOMETRIC METHODS.
Bolometer detectors containing thermal resistors which are less sensitive and require
higher biasing powers than those in Table 2 (references 7, 8, 27) can be used to measure
powers up to 100-200 mw. In general the methods are the same as those outlined above.
Alternatively, fixed or variable r-f attenuation of known value can be interposed between
the source and a low-power bolometer detector; this method is the more flexible since
power levels are restricted only by the power-handling capability of the attenuator. Since
attenuators capable of dissipating power up to several hundred watts (up to 1000 watts
in some designs) have been realized in practice, the power range inherent in this method
is at least 0-100 watts.
The attenuator's attenuation may be a significant function of frequency so that a
calibration should be made (or obtained from the known frequency characteristic) at the
measurement frequency. Interaction between the impedance of the source and the im-
pedance at the attenuator's input, and between the impedance of the detector and the
impedance at the attenuator's output, creates two sources of uncertainty in power measure-
ment (see Fig. 7). These impedance interactions are preferably reduced or eliminated
by an attenuator design which gives nearly unity match when alternate terminals are
terminated in unity match.
Errors from attenuator calibration instability with respect to time, ambient temperature,
power input level, and normal handling can usually be reduced to insignificance by (1)
selection of an appropriate type of attenuator, (2) careful attention to design and construc-
tion details, and (3) frequent recalibration when necessary.
The most stable fixed coaxial attenuator types have been (1) resistance-film center
conductor, (2) lumped-element TT or T pad, and (3) lossy dielectric. The first two types
are generally stable up to 1 watt; using lossy ceramics and heat-radiating fins type (3)
can be designed to handle 100-1000 watts stably. Lossy-dielectric flexible cables have
been generally unsatisfactory. In wave guides, resistance-film (parallel to the electric field)
types are used up to 1 watt, and lossy ceramic dielectric types up to 100 watts. In many
respects the most satisfactory fixed attenuators (in either coaxial or wave guide) have been
directional couplers. Attenuation stability is unquestionably high. Attenuations above
10-15 db give the best impedance characteristics. Stringent directivity requirements are
not necessary. Power-handling capability is limited solely, and input impedance primarily,
by the main line termination, which may be a useful load or a dummy load of the lossy
dielectric type (reference 15) or, for low powers, a resistance-film termination. The output
impedance is governed primarily by the low-power termination in the auxiliary guide.
It is practical to limit input and output impedance mismatches to 1.1 and 1.05 VSWR in
11-82 ELECTRICAL MEASUREMENTS
cent higher than that of the inlet water and the rate of flow is m grams per second then
w = 4.18m At watts. , , ,
Temperature rise is most sensitively indicated on a microammeter deflected by d-c
cm-rent generated by the differential action of series-connected thermoj unctions placed
alternately in the inlet and outlet water. The rate of now is kept nearly constant during a
measurement period by having a constant-head water source which is most simply a
continuously refilled container of water mounted a fixed height above the water load.
Calibration of the overall sensitivity can be accomplished by dissipating measurable d-c
or low-frequency power in a resistor which is immersed in, and therefore heats, the water.
A rate of flow different from that during measurement necessitates a proportional correc-
tion factor, so that relative flow rates must be checked. Alternatively, r-f power can be
continuously compared to the low-frequency calibrating power by using a balanced bridge
made up of thermoj unctions in the water on each side of the calibrating resistor and on
each side of the r-f water load; power measurement is then independent of water flow rate.
Uncertainties about the effects of spurious heat conduction must be eliminated by having
adequate thermal insulation between hot and cold junctions. Errors from heat lost by
air conduction, and thermal conduction down the line, are minimized by keeping the
temperature rise low (order of 1 deg cent), which requires a high rate of^fiow.^ Unfor-
tunately this reduces sensitivity so that either a large number of thermoj unctions or a
sensitive microammeter is required to avoid meter-reading error. For example, a specific
design using 16 hot and 16 cold junctions gave a 60-microampere deflection on a 10-ohm
meter for an input power of 20 watts when the rate of flow was 3 cc/sec.
High-Q matching transformers such as the simple, single, quarter-wavelength dielectric
retainer illustrated in Fig. 10, can match the water load to the transmission line satis-
factorily over only a narrow frequency band (VSWR within about 1.2 over ±3 per cent)
(reference 7), and the internally created high standing waves may cause arcing on high
powers. Low-Q, wide-band, matching methods are usually preferable and may be re-
quired. One such method is to couple the main transmission line (coaxial or wave guide) ,
by means of quarter-wavelength spaced holes (or slits) of progressively increasing sizes,
to an auxiliary line containing a longitudinal dielectric tube through which the water
flows; this tube forms the center conductor in coaxial line and is axially centered in wave
guide. Or a tapered water termination can be simply accomplished in wave guide by
mounting the wave-guide transmission line at a slight angle with respect to the horizontal.
Accuracy. Reflection loss and other r-f errors can be held to insignificant values by
suitable design. Power-measurement accuracy is governed primarily by errors in calibrat-
ing standards, meter reading, and thermal loss. These errors are reduced in practice to
values such that accuracies of 0.25-0.35 db are commonly attained for measurements of
power between 20 and 100 watts.
COMPARISON OF CALORIMETER AND BOLOMETER-ATTENUATOR POWER
READINGS. A calorimeter and bolometer-directional coupler attenuator combination
can be simultaneously excited by the same source; it is thus possible to compare readings
directly. Both devices, when carefully designed, are capable of such high accuracy that
cross-checks usually show differences no greater than the possible inaccuracy of the
attenuator calibration. If the calorimeter is the more reliable it can be used to calibrate
the bolometer-attenuator combination, which can then be used with equivalent accuracy
and greater convenience to measure high powers.
34. ATTENUATION MEASUREMENTS
Attenuation is defined as the ratio of the input to output power levels in a network
when it is excited by a matched source and terminated in a matched load. When the
latter specifications are met by the measuring circuit, uncertainties in the measured quan-
tity are avoided, but in actual use neither the source nor the load may be exactly matched.
To prevent uncertainties in its action under such conditions (see Fig. 7), accurately cal-
ibrated attenuators are usually designed to present nearly matched impedances when
alternate terminals are terminated with matched loads.
Attenuation is most accurately measured by insertion methods. Readings "are obtained
first without the unknown, then with the unknown inserted between a source and an r-f
detector (or mixer). To avoid impedance interaction errors (1) the r-f detector must be
well matched (by preceding it with a well-matched attenuator if necessary) , (2) the source
oscillator must be adequately decoupled, and (3) the source impedance must be well
matched. The last condition can be assured and additionally the source may be kept
stable during the measuring period by monitoring its output with a directional coupler
(see Fig. 4).
ATTENUATION MEASUREMENTS
11-83
Three methods for accurate attenuation measurement will be discussed: (1) comparison
against the calibrated law of a bolometer power meter, (2) comparison against a calibrated
i-f attenuator in a heterodyne receiver, and (3) comparison against a calibrated or known
r-f attenuator.
BOLOMETER POWER METER METHOD. The source is first terminated by the
bolometer detector, then by the attenuator whose output is terminated by the bolometer
detector. Attenuation is calculated from the ratio of the first to second power readings
on the power meter. Since only a ratio is involved, absolute powers need not be known;
therefore measurement accuracy is primarily limited by (1) meter-reading accuracy, (2)
bolometer detector law calibration, and (3) temperature (zero) drift. Limitation (1) is
the most important in measuring low attenuations (0-3 db) for which accuracies of ±0.05
db are practical. The accuracy of 3-13 db measurements is limited by (1) and (2) to about
±0.1 db. By using input and output power levels between 10 and Vs-Vio mw, attenua-
tions of 13-20 db are measurable within ±0.1 to 0.2 db accuracy which is controlled by
all three limitations.
HETERODYNE RECEIVER METHOD. In the heterodyne receiver method the input
to the second detector is kept constant by using a calibrated attenuator preceding the
intermediate frequency band-pass amplifier. I-f band widths of 0.1 to 3 megacycles with
center frequencies of 30 or 60 megacycles are commonly used. Attenuation is deduced
from two settings of the i-f attenuator, one with and one without the unknown between the
source and the mixer. Differential frequency stability requirements can be met by in-
corporating an automatic frequency control circuit, or, more simply, they can be materially
reduced by using a frequency-modulated mixer oscillator. Correct difference frequency
occurs simultaneously with peak output which is displayed on an oscilloscope or a d-c
meter preceded by a peak rectifier. Sweep methods permit the alternative use of video
instead of i-f amplification and calibrated attenuation.
The minimum signal which is accurately discernible in the presence of noise interference,
and the maximum signal on which the mixer is linear, usually bracket the maximum
measurable attenuation to about 50-70 db; such high-level differences cannot be accurately
measured unless high-level radiation and low-level pick-up are eliminated by carefully
shielding all joints in the transmission line and r-f components. For example, oscillator
tubes must be mounted in shielding containers into which power is supplied through r-f
filters (reference 17). Maximum signal levels for which the mixer operates linearly can
be determined by comparing its law against that of a bolometer power meter over a single
or consecutive 10-13 db ranges. In the ^.^^^^^
R-f inT" ^""-SiTa 0¥ "IR-f-OBt
linear region a power meter, monitoring
and indicating relative r-f signal levels,
can also be used to calibrate or cheek the
i-f attenuator. Attenuations between 0
and 60 db are measurable with an accu-
racy of ±0.1-0.2 db with heterodyne re-
ceiver methods.
R-F ATTENUATOR METHOD. In
the calibrated r-f attenuator method all
questions about linearity are eliminated,
since the input power to the first detector
(or mixer) is held constant. Attenuation
of the unknown is deduced from two set-
tings of the r-f attenuator, one before and
after insertion of the unknown.
A calibrated variable r-f attenuator
may be a resistance-film type (reference
27) (one for wave guide is illustrated in
Fig. 11), variable between 0 and 40 db by
a precision mechanism which can be ca-
pable of a combined setting and reading
accuracy of ±0.1 db. Such attenuators
must be calibrated and should be checked
periodically by some other, more funda-
mental method, which may introduce an
additional error of ±0.1 db. However,
the importance of this lack of accuracy is often outweighed by considerations of the con-
venience inherent in (1) measurement of unknown attenuation by r-f attenuator com-
parison methods, and (2) use of resistance-film attenuators in them.
The most stable variable attenuator standards are of the wave-guide-below-cutoff type,
Res&fance
film terminations i
A* Befaw-cutoff type for coaxial line:
R-f in I
B. Below-ouioff type used
with waiteguide lines
Resistance film
C. Resistance-f tJm type for waveguide Ooes
FIG. 11. Variable Attenuators
11-84
ELECTRICAL MEASUREMENTS
and these are the only types for which incremental attenuation ratios can be calculated
in advance (references 21 and 15). Measurement of unknown attenuation by comparison
against such an attenuator is therefore a fundamental method. Unfortunately^the min-
imum loss, above which the attenuation law is calculable without uncertainty, is around
20-30 db and may be higher if input and output impedances are corrected by using masking
attenuation (reference 27). Below-cutoS attenuators therefore require the use of high-
sensitivity indicators which may be (1) heterodyne receivers or (2) simply low-frequency
band-pass amplifier detectors for which the signal must be amplitude modulated. The
noise level may be higher in the latter system, but it is more conveniently used since
only one r-f signal source is required. Accuracy is primarily limited by (1) imperfections
in the attenuator mechanism, (2) indicator time stability, and (3) impedance interaction.
In practice these factors have been controlled sufficiently well to allow ±0.2 db accuracy
for 0-40 db attenuation measurements.
35. FREQUENCY MEASUREMENTS
Two general methods can be used to measure frequency: (1) direct comparison with
harmonics of a known frequency source (reference 22) (heterodyne frequency meter
method), and (2) resonance in a tunable resonator (wavemeter method). Except where
the highest accuracy is needed, method (2) is the more practical since measurements can
be made quickly and with the ramimurn of equipment. A transmission line propagating
the unknown frequency is coupled to the resonator which is adjusted to resonate at that
frequency; resonance is indicated by the response of a detector of relative power level
in a load which terminates the transmission line.
Transmission-line resonators can be constructed to be self-calibrating by incorporating
enough linear motion so that the positions of several resonances separated by half-wave-
lengths can be measured (lecher wire method). However, the calibration accuracy is
only about 1 part in 103. The more accurate practice is to incorporate just enough travel
to cover the desired frequency band and to calibrate the resonator by method (1) above;
in this manner absolute accuracies of 1 part in 10* can be obtained.
RESONATORS. Resonators can be divided into two general classes: (1) resonant
transmission lines (coaxial or wave guide) , and (2) resonant cavities. Resonant transmis-
sion lines are shorted at one end and
CoBtanf fTnger| _Sca"le
Antf.--backlash Spclng
-A.. Coaxial resonator
Cross-po!acJ2at)on
suppression loop
Sea
djustmg the line length to
the other end where it is open or
short-circuited. Resonant cavities
are tuned by adjusting a reactance
(physical discontinuity) in the elec-
tromagnetic field. On transmission-
line resonators the calibrated line
length changes almost linearly with
transmission-line wavelength (refer-
ence 1); one specific type of cavity
resonator, really a hybrid combina-
tion of TM010 cavity and coaxial
line, can be constructed to have a
nearly linear calibration versus fre-
quency over a band width as great as
12 per cent (reference 24) .
Table 4 illustrates underlying re-
quirements to be met for accurate
frequency measurement by listing
the general characteristics of two of
the simplest types of transmission-
line resonators (Fig. 12) . These res-
onators are designed for approxi-
mately optimum performance when
diameters are limited so that only
the dominant mode (reference 1)
,. (Section 7) can propagate. Coaxial-
une resonators are generally satisfactory in the 1500-10,000 megacycle range* wave-
guide resonators are superior in the 10,000-25,000 megacycle range where the Q of
coaxial-line resonators become too low. In this latter range wave-guide resonators using
the TEQ1 mode and special mode suppression techniques can be used to attain higher
Loss/ dielectric-
masking bearing
contact
lash spun?
S. Te<H moder resonator
FIG. 12. Wavemeter Resonators
FREQUENCY MEASUBEMENTS
11-85
realizable Q's (see Section 7), but the advantage -will be slight unless corresponding
improvements can be introduced to reduce errors caused by imperfections in the tuning
mechanism.
WAVEMETERS. The combination of a resonator coupled to a section of transmission
line (to which an unknown frequency source and a detector can be coupled) will be desig-
nated as a wavemeter. Wavemeters are classified according to the way the resonator
tuning affects transmission: (1) transmission type, and (2) suppression type. For the
first type, the resonator must contain two orifices, probes, or loops, which allow the
resonator to be connected in tandem with the transmission line; at resonance, power is
transmitted through the resonator, and resonance is indicated by a maximum response on
the indicator. The second type employs a single orifice, probe, or loop, to couple the res-
onator's impedance into the transmission line. The coupled impedance tends to suppress
the resonant frequency which is indicated by a minimum response on the detector.
Table 4. Typical Wavemeter Characteristics
Frequency
Band Limits
Theo-
retical
n
Realiz-
able
r\
Possible Errors from
Imperfect Selectivity,
Imperfect Tuning
Quarter
Wave-
Inside Dimensions:
Diameters and
HJ
Factor
y
Factor
Mechanism, Impedance
Mismatch
length
Lengths
Me
Q
Qcb
Aft
Me
A/m
Me
A/z
Me
N
di
in.
ds
in.
I
in.
Coaxial line
1,500
9,200
8,000
0.01
0.03
0.01
3
0.65
2.35
5.90
2,500
11,500
0.02
0.07
0.01
3.54
3,600
7,500
7,000
0.04
0.09
0.03
5
0.32
1.20
4.14
5,000
8,400
0.05
0.2
0.04
2.95
8,500
5,800
3,500
0.2
0.2
0.1
11
0.16
0.59
3.83
10,000
6,200
0.2
0.3
0.1
3.24
19,100
4,300
1,800
0.8
0.6
0.5
19
0.08
0.29
3.10
20,000
4,400
0.9
0.7
0.6
2. SO
22,800
3,800
1,200
1.5
0.8
1.0
21
0.06
0.23
2.72
25,000
3,900
1.6
1.0
1.0
2.48
TE 1 1 mode round
wave guide
2,060
23,000
20,000
0.01
0.01
2
3.62
7.3
2,500
25^000
0.03
5.6
4,390
19,000
17,000
0.02
0.2
0.01
4
1.81
5.5
5! ooo
2l!oOO
0^6
3.6
9 050
15 000
10,000
0.08
0.07
0.05
6
0.90
3.6
io!ooo
OJ5
2.7
18 700
1 1 ,000
7,000
0.2
0.2
O.I
10
0.45
2.7
20 ',000
OM
2.3
72 ynn
10 000
5 000
0.4
0.3
0.2
12
0.36
2.5
J.J , / UU
25,000
<K5
2.1
Transmission-type wavemeters are not favored for general frequency measurement,
primarily as a result of the characteristic lack of energy transmission unless the tuning
is adjusted for near-resonance. Failing to find a response on the detector, the operator is
faced with uncertainty as to the adequacy of the power output of the source or the sensi-
tivity of the detector, and this is especially troublesome if either or both must also be
tuned. A suppression type is capable of just as accurate frequency measurements, and
it is more convenient to use.
FREQUENCY MEASUREMENT WITH SUPPRESSION-TYPE WAVEMETERS.
The simplest arrangement for measuring frequency on a transmission line is that shown
in Fig. 13 A. In the process of measuring frequency the impedance to the source is altered,
and this may change its frequency unless avoided by keeping adequate attenuation be-
tween the oscillator and wavemeter. Normal operating conditions are restored by detun-
ing the resonator. In good designs a detuned wavemeter should not create a VSWB in
excess of 1 . 1 . This circuit finds a wide application where only a spot check on the frequency
of low-power sources is needed. Figure 13B shows an arrangement for continuously
monitoring frequency with a negligible disturbance of energy level and impedance condi-
tions in the main transmission line. In some cases it may be more practical to couple the
auxiliary to the main transmission line by means of a single orifice, probe, or loop, but a
directional coupler is preferred because less masking attenuation is needed for the wave-
meter to operate out of a matched impedance, a condition for which it is calibrated.
11-86
ELECTRICAL MEASUREMENTS
Wavemeters should be calibrated and operated only in nearly matched circuits because
reactances introduced by the source, or load, or both, change the frequency of minimum
response. Using the lumped-element equivalent circuits in Fig. 14 for analysis the
magnitude of frequency change can be estimated from: 8A/^0& = /(^« + #1), wnere
the mismatched source and load introduce impedances having normalized susceptance
components B8 and BI at the plane of the resonator coupling. By using masking attenu-
ators wherever necessary, it is usually practical to limit both the source and bad impedance
mismatch to 1.2 VSWR; highest value for (B. + Bi) = 0.4. The errors in Table 4 were
computed on this assumption and on the assumption that the wavemeter was calibrated
in a perfectly matched transmission line.
The mechanical system used for tuning and indicating the resonant frequency contains
potential' sources of predominant error. The error in interpreting resonant frequency
from a scale reading can be estimated from: A/m = ±Mbl, where U is the rate of change
of resonant frequency with tuning plunger movement in megacycles per men and A£ is
Oscillator X V | Load
i_j j p.
Attenuator Wavemeter
A.. Spot measuremerd:
Source
Probe
A.. Probe coupling
Resonator
Loacf
Source DirectkmaJ coupler Load
J3. Frequency monitoring
FIG. 13. Frequency Measurement Cir-
cuits
Transmission
line
B. Orifice coupling
Coupling
orifice
FIG. 14. Approximately Equivalent
Lumped-element Circuits
the maximum possible sum of (1) backlash between the driving mechanism and the scale,
(2) non-linearity in driving mechanism between calibration points, and (3) uncertainty
in reading the scale. In Table 4, AZ was assumed as 0.0001 in.; even with this high order
of mechanical precision the errors are large. These errors can be lowered by reducing M
(band spreading). In resonant-line resonators this can be accomplished by increasing n,
the number of quarter or half wavelengths. However, a compromise is usually made
between tolerable error and the frequency range for which all resonant settings are unique.
An alternative method for band-spreading wave-guide resonators is to operate near cut-off
frequency for the resonant mode (reference 1) ; but this restricts band width more than
the first method.
Both the resonator's Q factor and the tightness with which it is coupled to the trans-
mission line influence the selectivity of response in the detector. Using the circuits in
Fig. 14 for analysis it can be shown that the possible error in tuning the wavemeter result-
ing from inability to discern the absolute minimum response on a power indicator is:
(3)
where Qab is the Q of the total impedance between terminals a-b (not the "loaded Q") ;
Qa& is always less than the theoretical Qi (reference 1), and typical values for copper
resonators, based upon experimental data (A = 2), are shown in the table. The suppres-
sion loss ratio, A, is the ratio of the power in the load when the resonator is completely
detuned, Pm, to the power in the load when the resonator is tuned. The minimum dis-
cernible change in power expressed as a fraction of the detuned power is AP/Pm. This
equation is accurate only for AP/Pm below about 10 per cent. Assuming that Pm gives
full-scale deflection and that a power change of 0.5 per cent of full scale can be discerned,
Table 4 gives the possible errors for some typical resonators.
Differential Accuracy. For well-constructed wavemeters the exact calibration curve is
everywhere smooth and regular. If terminating reactances remain constant the accuracy
in measuring small frequency differences is primarily limited by the last two factors above.
FREQUENCY MEASUREMENTS
11-87
)-80OMc
5 watts
Microwave frequency
1500-25,000 Me
— 2D to —40 dbm
j / Directional coupler
L
1 4-
jf
E£-
Crystal detector '
harmonic generator -
Directional
coupler -
" p^. ¥M Crystal
-o mixer
\ §
•A c
* ~Z Crystal
-< , /"""N detector
) Attenuator ^ J Attenuator
,
m,
• ""[ . &Z&&7 -^S^^f
""LJ
1
Klystron local *
oscillator
"*-• — Repeller
Wavemeter
under test
|
Sawtooth
sweep
—3
^ Oscillos-
COpe
2-5QJ<c
amplifier
«
hign^gam
Each one of these errors can enter twice. According to Table 4, differential measurements
can be made with an accuracy no worse than about 1 part in 104. Accuracies of 5 in 10s
are commonly realized in practice.
"Wavemeter Calibration. Three somewhat different methods can be used to calibrate
the wavemeter against low-frequency standards. In the first method the wavemeter is
adjusted to resonate at a c-w frequency supplied by a local microwave oscillator; this
frequency is then measured with a precision heterodyne frequency meter (accurate to 1
part in 106) such as shown in reference 22.
In the second method, microwave frequencies standards are harmonically generated
from low-frequency standards; a calibration is then made by adjusting the frequency*meter
to resonate on these standards (reference 27). The response must be detected in a high-
gain low-noise detector such as a dou-
ble-detection receiver, since the har-
monics power output is very low.
The third method is illustrated in
Fig. 15, which combines advantageous
features of both the above methods.
The microwave oscillator is frequency
modulated by a saw-tooth wave on its
repeller (references 9 and 10) . Its cen-
ter frequency is adjusted until a low-
amplitude marker oscillation appears
superimposed on the rectified envelope
of the oscillator output; this pip ap-
pears during the time interval for
which the frequency zero-beats (2-50
kc) with a standard frequency gener-
ated by the crystal rectifier multi-
plier. The frequency meter is tuned
until its null brackets the marker pip.
Frequency-time stability of the f-m
oscillator is unimportant, and the low-
level output from the harmonic gener-
ator is used only for frequency mark-
ing. Additionally, a known c-w cali-
brating frequency can be obtained by
gradually reducing the sweep to zero
while keeping the marker in the center of the mode; a beat note in the head phones can
be tuned in and retained by trimming adjustments on the frequency.
Conventional methods employing a master crystal-controlled oscillator and vacuum-
tube multipliers can be used for generating the standard frequencies up to 800 megacycles
(see p. 7-92). These frequencies are then multiplied 20 to 60 times in a silicon crystal
rectifier mounted in the microwave transmission line. The harmonic number can be easily
identified by a roughly calibrated or self-calibrating wavemeter. High burn-out crystals
(reference 6) are recommended since they handle more input power. The microwave
signal power so produced is of the order of -20 to -50 dbm. A severe requirement is
therefore placed upon the noise figure of the high-gain detection system used to amplify
the response to a usable amplitude.
Absolute Accuracy. By the above methods standard frequencies can be known to an
accuracy of 1 part in 106. Adding to this the accuracy with which these standard frequen-
cies can be transferred to the wavemeter calibration curve (limited primarily by the first
two errors listed in Table 4) results in a typical absolute calibration accuracy of about 5
parts in 105. Then, assuming that corrections for temperature and humidity can be made
with negligible error, adding aU three errors in Table 4 to the calibration accuracy, a typical
wavemeter can be used to measure frequency with an absolute accuracy of 1-2 parts in 10 .
Correction for Temperature and Humidity. In order to interpret the resonant frequency
from a scale reading and the calibration chart accurately, corrections must be made to
allow for the effects of any change from the reference temperature and humidity conditions
under which the resonator was calibrated. Two effects operate independently, and the
corrections for them can be computed separately, then added algebraically: (1) tempera-
ture changes induce thermal expansion or contraction of the resonator's internal dimen-
sions; (2) combined temperature and relative humidity changes vary the dielectric constant
of the air inside unsealed resonators (reference 28).
The correction for thermal expansion of homogeneous resonators can be computed from:
A/ = — C/o A£, where A/ is the frequency correction to be added to the resonant frequency
Head phones
Harmonic j Spread
marker j scale
Wavemef er tuned
FIG. 15. Wavemeter Calibration Circuit
11-88
ELECTRICAL MEASUREMENTS
/o indicated by the calibration chart, Ar is the change in temperature from that for which
the calibration chart was prepared, and C is the coefficient of linear expansion for the
resonator material. The correction is small for resonators made of Invar; A///O is about
d=5.5 X 10 ~7 for ±1 deg fahr temperature change. For the same temperature change
A///O is about ±6.6 X 10~6 for steel resonators, and ±1 X 10"5 for brass resonators.
Corrections for the effect of dielectric constant changes are given in Table 5, which
applies for unsealed resonators operated at sea-level atmosphere (reference 27). The
corrections are to be algebraically added to the indicated resonant frequency (assuming
that the calibration was made, or normalized, for 25 deg cent and 60 per cent relative
humidity conditions). It will be observed that for ±10 per cent change in relative
humidity the correction is dbl.3 X 10 "^ at 25 deg cent.
Table 5. Resonant-frequency Correction for Humidity Changes in Unsealed Resonators
Temper-
ature,
deg cent
Relative Humidity, per cent
Temper-
ature,
deg fahr
20
30
40
50
60
70
80
90
100
0
+0.0050
+0.0045
+0.0042
+0.0050
+0.0038
+0.0035
+0.0032
+0.0028
+0.0025
32
5
+0.0052
+0.0048
+0.0042
+0.0040
+0.0035
+0.0032
+0.0027
+0.0022
+0.0018
41
10
+0.0055
+0.0049
+0.0042
+0.0038
+0.0031
+0.0025
+0.0020
+0.0013
+0.0008
50
15
+0.0055
+0.0048
+0.0041
+0.0032
+0.0024
+0.0015
+0.0010
+0.0001
-0.0006
59
20
+0.0055
+0.0045
+0.0035
+0.0025
+0.0015
+0.0005
-0.0006
-0.0015
-0.0025
68
25
+0.0055
+0.0041
+0.0028
+0.0013
+0.0000
-0.0013
-0.0025
-0.0040
-0.0055
77
30
+0.0050
+0.0032
+0,0025
-0.0003
-0.0018
-0.0038
-0.0052
-0.0071
-0.0080
86
35
+0.0045
+0.0023
+0.0002
-0.0022
-0.0045
-0.0067
-0.0089
-0.0100
-0.0133
95
40
+0.0030
+0.0010
-0.0018
-0.0047
-0.0075
-0.0105
-0.0131
-0.0158
-0.0188
104
45
+0.0027
-0.0007
-0,0043
-0.0078
-0.0115
-0.0150
-0.0186
-0.0221
-0.0256
113
50
+0.0014
-0.0031
-0.0075
-0.0119
-0.0163
-0.0209
-0.0252
-0.0295
-0.0340
112
Frequency correction, per cent to be added to indicated reading, for resonators calibrated at 25 deg cent and 60 per
cent relative humidity.
Frequency Tuning. Suppression loss ratios lower than 2 increase the difficulty in
finding the region of resonance when the response is indicated on a d-c meter; since meters
are inherently sluggish the narrow resonant region can be easily missed. For example,
the resonant region in terms of band width between the two frequencies for which the power
change is half the total null change is only A/Q0& = /VZ". On wide-range wavemeters it
is often desirable to keep this resonant region relatively wide by purposely designing for
only a moderate value of Qab-
High-suppression moderate-Q requirements are relatively unimportant when a-m
(including pulsed) wave envelopes are displayed on an oscilloscope screen. Since oscillo-
scopes respond to rapid level changes a reaction can usually be discerned, even though the
resonant region be tuned through rapidly. In some cases suppression-loss ratios as low
as 1.1 to 1.2 may be desirable in order to avoid excessive distortion of the oscilloscopic
pattern in the region of resonance.
The oscilloscope pattern in Fig. 16 illustrates the superposition of a wavemeter null
("pip") at two frequencies on the envelope of the output of a klystron oscillator which is
being frequency and amplitude modulated by a sawtooth voltage
on its repeller (reference 9). The "pip" can so easily be located
on this type of wave that auxiliary facilities comprising an adjust-
\ J able sweep voltage and a crystal detector with oscilloscope indi-
X / cator provide a convenient method for quickly tuning klystron
FIG. 16. Wavemeter sources to required c-w frequencies (as set on the wavemeter).
"Pips" on Klystron Mode The initial sweep voltage is large enough to sweep through an oscil-
lation mode completely, regardless of the initial settings of the
oscillator tuning controls; tuning is adjusted until the wavemeter pip appears at the top
of the mode. The sweep voltage is then gradually reduced to zero and the oscillator
tuning controls are simultaneously adjusted to keep the "pip" centered on the mode.
BIBLIOGRAPHY
1. Schelkunoff, S. A., Electromagnetic Waves, D. Van Nostrand Co., New York, 1943
o iiven * ' Communication Engineering, McGraw-Hill Book Co New York 1937
A Q ° StPr?^* V* T * Technique* of Microwave Measurements, McGraw-Hill, New' York 1947
4. Smith, P. H., An Improved Transmission Line Calculator, Electronics January 1944
n"*" Publication 23-80, Sperry Gyroscope Co., 1944.
Uectronic$r July 1946, p. 112.
OSCILLATORS FOR SIGNAL GENERATOR USE 11-89
?' ^^yton, R.J., et al., Radio Measurements in the Decimeter and Centimeter Wavebands, /. I.E.E.J
8. Becker, J. A et al., Properties and Uses of Thermistors— Thermally Sensitive Resistors, BeU
bys. Tech. J., January 1947.
9. Pierce, J. R Reflex Oscillators, Proc I.R.E., Vol. 33, 112 (February 1945).
10. Genzton, E. L and Harrison, A. E., Reflex-klystron Oscillators, Proc. I.R.E., VoL 34 (March 1946).
11. iiske, J. B., et al., The Magnetron as a Generator of Centimeter Waves, Bell Sys. Tech. J., Vol. 25
(.April 1946) .
12. HasseU, FM and Jenks, F., Electroforming Microwave Components, Electronic^ March 1946.
}* ££ i J1 ^ral^rProbe Error m Standing-wave Detectors, Proc. I.R.E., Vol. 34, 33P (January 1946).
14. Mumford, W. W., Directional Couplers, Proc. I.R.E., Vol. 35, 160 (February 1947).
J5* S^?n' E- IV « al" Microwave Radar Testing, Trans. AJ.E.E., Vol. 65, 274 (May 1946).
16. Whinnery, J. R.T et al., Coaxial Line Discontinuities, Proc. I.R.E., Vol. 32, 695 (1944).
17. Ragan, G. L., Microwave Transmission Circuits, McGraw-Hill, New York, 194S.
18. Tyrrell, W. A., Hybrid Circuits for Microwaves, Proc. LR^E., Vol. 35 (November 1947).
19. Type 821 Barretter, Technical Data Bulletin, Sperry Gyroscope Co.
20. Guillemin, E. A., Communication Networks, John Wiley & Sons, New York, 1949.
21. Lindner, E. G., Attenuation of Electromagnetic Fields in Pipes Smaller Than Critical Size, Proc.
I.R.E., Vol. 30, 554 (December 1942).
22. Essen, L., and Gordon-Smith, A. G., The Measurement of Frequencies in the Range 100 Mc/s to
10,000 Mc/s, J. I.E.E., Vol. 92, Part III, 291 (December 1945).
23. Essen, L., The Design, Calibration, and Performance of Resonance Wavemeters for Frequencies
between 1000 and 25,000 Mc/s., J. I.E.E., Vol. 93, Part IIIA., No. 9, 1946.
24. Essen, L., Cavity-resonator Wavemeter — Simple Types of Wide Frequency Range, Wireless
Engineer, Vol. 23, 126 (May 1946).
25. Swedin, M., Directive Couplers in Wave Guides, J. I.E.E., Vol. 93, Part IIIA, No. 4, 1946.
26. Rosen, S., and Bangert, J. T., A Consideration of Directivity in Wave Guide Directional Couplers,
Proc. I.R.E., Vol. 37 (April 1949).
27. Gaffney, F. J., Microwave Measurements and Test Equipments, Proc. I.R.E., Vol. 34, 775 (October
28. Englund, C. R., et al., Further Results of a Study of Ultra-short-wave Transmission Phenomena,
Bell Sys. Tech. J., Vol. 19, 369 (July 1935).
SIGNAL GENERATORS AND POWER MEASUREMENT
By F. J. GafEney
A signal generator is a source of alternating voltage, calibrated in frequency and voltage
(or power output into a specified load), and with good modulation characteristics, and
carefully shielded. Units are commercially available which collectively cover frequency
ranges from audio to microwave frequencies. Designs are, in general, made as broad band
as the limitations of oscillator-tube and power-output calibration devices (including the
output attenuator) will allow. Problems encountered in the design of signal generators
are: (1) the design of stable oscillator circuits, (2) the design of systems of modulation, (3)
output voltage or power standardization, (4) attenuator design, (5) shielding.
36. OSCILLATORS FOR SIGNAL GENERATOR USE
Signal generator oscillators are designed for maximum frequency stability with tempera-
ture and line voltage. Wherever possible it is desirable to load the oscillator lightly. For
this reason it is advantageous at some frequencies to employ buffer amplifiers which feed
the output circuits rather than to feed these circuits directly from the signal generator
oscillator itself.
Tubes and Circuits. Any oscillator consists essentially of a tuned amplifier with suffi-
cient positive feedback to supply the grid losses. The frequency stability depends on the
frequency shift necessary to restore proper
phase in the grid circuit when the tube char- Ganged CQndens
acteristics change as the result of line voltage, -^
thermal effects, etc. This frequency shift is a \ .^wvvlf ? » Output
function of the Q of the tuned circuit em- v ^^
ployed, of the feedback system used, and of
the method of coupling to the tube.
AUDIO-FREQUENCY OSCILLATORS.
For the range from a few cycles to 20 kc or ^"T~* ^Biasing lamp
more, various forms of rC oscillators have 1
proved advantageous. This type of oscillator -i
is essentially an untuned amplifier with an p^ ^ wien Bridge Oscillator
rC filter providing the tuned feedback. The _
filter may be of the twin T or Wien bridge type. A diagram of the latter is shown in Fig. 1.
" > sharpness of the filter, which in turn depends on
11-90
ELECTRICAL MEASUREMENTS
/,-£
R-f
iUier
Audio
ajnplifier
the tracking of the tuning condensers. Means are usually incorporated for providing an
automatic bias on the oscillator tube to insure Glass A operation as the oscillator output
changes over the frequency band. This can take the form of a non-linear resistance such
as a tungsten lamp in the cathode circuit of the oscillator. This type of oscillator if properly
designed can be made extremely stable and pure in waveform. One disadvantage is the
inability of a single tuning condenser to cover a large frequency range. For this reason a
step switch is usually provided which switches the resistances in the circuit to provide
multiple ranges.
For wider-range low-frequency oscillators (from a few cycles to several megacycles per
second) beat-frequency oscillators may be used. A block diagram of such an oscillator is
shown in Fig. 2. It consists essentially of two r-f oscillators, one fixed and one variable,
Output to
" attenuator
FIG. 2. Block Diagram of Beat Frequency Oscillator
which feed a mixer tube. The difference frequency between the r-f oscillators is then fed
through an r-f niter to an audio amplifier. This type of circuit has the advantage that a
very large frequency range can be covered with small changes in the frequency of the vari-
able r-f oscillator. Its main disadvantage is that the audio frequency is the difference be-
tween two radio frequencies so that a small percentage variation in one of these frequencies
will produce a relatively large variation in the output frequency. However, both r-f oscil-
lators can be designed so as to be very similar in construction, and under these conditions
they have a tendency to drift together so as to minimize the drift in the audio frequency. A
serious problem which exists in the design of this type of oscillator is concerned with spuri-
ous outputs produced by the beating of harmonics of the r-f oscillators. These effects can
be minimized by utilizing pure r-f waveforms, by the use of suitable filters between r-f
and mixer stages, and by careful mixer design for large signal mixing.
RADIO-FREQUENCY OSCILLATORS. For the range of frequencies up to about 100
megacycles per second, conventional lumped constant circuits may be used. Several types
of circuits such as those described in Section 7 may be employed. In order to obtain good
frequency stability, either impedance-stabilized oscillators or oscillators of the electron-
coupled type should be used. With the latter type of oscillator, frequency variation de-
pends on the ratio of the screen-grid voltage to the plate voltage, and for some value of
this ratio the frequency variation is extremely small with variations in plate voltage.
The electron-coupled oscillator, though good from the standpoint of stability, produces a
poor waveform which contains many harmonies. Care must therefore be taken in the use
of such an oscillator to insure that the harmonic content does not affect the power-measur-
ing circuit or the receiver being tested. The frequency stability of all types of oscillators
is improved by regulation of the B voltage. Some frequency instability can be produced
by variation in cathode heater voltage, but this is seldom compensated for in practical
design. Frequency stability with variation in ambient temperature is accomplished
through careful design of the tuned circuit of the oscillator. Coil forms should be wound
on a material having a very low coefficient of expansion,
such as Vicor. Special attention must be paid to the de-
sign of the variable condenser to minimize dimensional
changes with temperature.
At frequencies above 100 megacycles per second con-
siderable difficulty is encountered in the use of conven-
tional lumped circuits. The losses in such circuits be-
come excessive at these frequencies, and the tuning range
becomes small, since, as the inductance is decreased to
obtain higher frequencies, the tube and wiring capaci-
tances become a larger proportion of the total allowable
capacitance. One solution to this problem has been in
the use of circuits of the butterfly type such as that shown
in Fig. 3. Here the inductance and capacitance are varied simultaneously. This has
the effect of increasing the tuning range and simultaneously maintaining the L/C ratio.
Such circuits have been built for frequencies up to 2000 megacycles per second. At
frequencies above 1000 megacycles per second, however, the losses are too great for
practical oscillator applications.
FIG. 3. Butterfly Tuning Circuit —
400 to 1200 megacycles per second
(Courtesy of General Radio Co.)
OSCILLATORS FOR SIGNAL GENERATOR USE 11-91
in heo?™?11 10 ^ Pr°bl6m °f obtaitting toned circuits at high frequencies consists
Here Sati™ Tff T* -°f tr*nsmission ^ « in the use of cavity-type resonators.
' t« flow T ^ ehmmated and the distributed nature of the circuit allows cur-
nne lenTh fT f^' ?""? Permitt^ 1™ copper losses. For a lossless trans-
hne length I, short-circuited at the far end, the input impedance *,-„ is given by:
. ATTL
• ZQ tan — —
A
(1)
*° .77cllaracteristic impedance of the Hne and X = wavelength
«nHSf n~f / 4' \= u°°.' ACtUally' Owing to losses' transmission lines dissipate energy
and have a Q factor which is defined in terms of band width as in a lumped constant circuit.
.transmission line Q is approximately given by:
where/o = frequency of resonance (cycles per second), ^ = characteristic impedance =
V L/C (ohms), r = resistance per unit length (ohms/meter), and c = velocity of light
(meters per second) .
The input impedance of a quarter wavelength short-circuited line is then approximately
given by:
In the equation for Q, both SQ and r vary with the dimensions of the hne. For maximum Q
there exists an optimum diameter ratio for coaxial lines (for conductors of the same resis-
tivity) amd an optimum ratio of spacing to the diameter of the conductors for parallel
wire lines! Letting this ratio be b/a for the two cases, one value of b/a, gives maximum Q
and a second value gives maximum input impedance. The values, together with the
corresponding characteristic impedances are given in the table.
COAXIAL LINES
b/a
Max. Q.. ., 3.6
Max. z 9.2
zo
76.8
133,1
5/o
4.0
8.0
WISE LINES
20
851.
1934.
With b/a constant, both Q and z increase linearly with b. Such a line can then be used
as an antiresonant circuit, with the resonance frequency determined by the line length.
Actually the shapes of the curves of reactance and resistance as a function of frequency
are not identical to those of lumped constant circuits but are quite similar near the resonant
frequency. Parallel wire transmission lines, because of then* simplicity of construction,
are sometimes used in experimental oscillators, but coaxial transmission lines are more
commonly used in signal generator applications because of their lower losses (the radiation
• loss being zero) and self-shielding construction. The only difficulty with such resonant
lines is in the physical lengths required and in the mechanical difficulties with sliding
contacts. For a frequency of 100 megacycles per second, for instance, a quarter-wavelength
transmission Hne would have a length of 75 cm. The Hne may, however, be artificially
shortened by the use of a fixed condenser across its input terminals.
Vacuum tubes designed for low-frequency appHcations fail at higher frequencies because
of losses, Hmitations due to input and
output capacitances, and transit time [< — — 1« H Alternate method PutJ
effects. To minimize these defects, $$ ( ^f output coupling f
special tubes have been designed for
the higher-frequency ranges. By mak-
ing the tube elements very small, spac-
ings between elements can also be
made small without the introduction
of excessive interelectrode capaci-
tances. Lead inductances may be
minimized by bringing out more than
one lead from each electrode as in some
types of high-frequency acorn tubes.
A better scheme is that exemplified by tubes of the 2C40 type which utilize disk seal
construction to reduce lead inductances to a minimum. This type of oscillator tube lends
itself particularly well to incorporation into a coaxial-Hne oscillator circuit. One such
design showing a tuned plate-tuned grid oscillator is shown in Fig. 4. Owing to the
difference in end effects and to the capacitive loading contributed by the tube elements,
FIG. 4.
Input
Typical Double-concentric-eavity Circuit
(Courtesy of General Electric Co.)
11-92
ELECTRICAL MEASUREMENTS
it is usually necessary to move the tuning plungers at a different rate. This causes some
difficulty with mechanical tracking of the two cavities.
An alternative design known as a reentrant oscillator is shown in Fig. 5. This type of
oscillator may be controlled by means of a single tuning plunger but will operate satis-
factorily only over a relatively narrow fre-
quency band. Oscillators using this type of
circuit with a 2C40 triode tube have been made
for frequencies as high as 3000 megacycles per
second. Experimental tubes have been made
to oscillate in this type of circuit at even higher
frequencies. Because of the close grid cathode
FIG. 5. Method for Tuning Re-entrant Oscil- spacing a considerable frequency variation may
lator Circuit (Courtesy of General Electric Co.) be produced by variations of the tube heater
voltage.
At frequencies above 2000 megacycles per second, velocity variation tubes become useful.
In this type of oscillator tube transit time is utilized to provide bunching of the electrons
in a drift space. The efficiency of this type of oscillator is low and the frequency stability
is relatively poor. No upper frequency limit exists for oscillators of this type except that
imposed by problems of physical construction. This limitation occurs somewhere in the
region of 60,000 megacycles per second. .
Cavity resonators which may either be fj)
external to the tube or integral with it ' '
are utilized with this type of oscillator.
The type of cavity resonator used is one
which develops maximum voltage across
the bunching grids in the tube.
The type of velocity variation tube
known as a reflex oscillator is most con-
venient for signal generator applications.
An outline diagram of this type is shown
in Fig. 6. In this tube the electron
stream is velocity modulated by the
bunching grids. The electrons then
drift in a space between the bunching
grids and a negatively charged reflector
which turns them around and causes
Output coupling'
loop
,,Tlmhig plunger
.Reflector
. ^Drlft space
'Resonator ana's
•Eleclfoj5 gun
•Glass envelope
FIB. 6. Reflex Type Velocity Variation Oscillator
bunches to arrive again at the bunching grids in such phase as to deliver energy to the
cavity resonator of which the bunching grids form a part. The resonant frequency of such
an oscillator may be changed by varying the cavity dimensions. Alternatively, the fre-
quency may be changed by changing the capacitance between the buncher grids. The
latter method requires that the tube be built with a flexible diaphragm since the grids are of
Fro. 7. TM-mode Cavity for Reflex Velocity Variation Oscillator
course in an evacuated space. The realizable tuning range with this type of tuning is only
about 20 per cent. This design does, however, possess the advantage that the tube and
the circuit are self-contained and troubles with sliding contacts are eliminated.
By bringing the bunching grids out through disk seals in a glass envelope an external
eavity may be used with this type of tube. Cavities of both coaxial mode and the TM
MODULATION OF SIGNAL GENERATORS
11-93
mode have been employed successfully. A cavity of the coaxial-mode type is shown in
±"ig. t>; .tig. 7 snows an outline drawing of the TM-mode cavity. With the coaxial-type
cavity frequency ranges of better than 2 to 1 may be achieved, Care is again necessary
in the construction of tuning plungers so as to make good contact over the tuning range.
In order to minimize rubbing contact, it is possible to design choke-type contacts which
are themselves resonant sections of transmission lines.
ibilizing /-Audio bypass
/. condenser
, ^Stabiliz
/ //Condenser ,'j_
•Xr — r^W-C*
R-f choke f
37. MODULATION OF SIGNAL GENERATORS
In order to test the detection characteristics of receivers and to supply a signal that can
be amplified by audio amplifier methods, signal generators are usually equipped with means
for modulating the r-f voltage output. Several types of modulation are used, depending
on the types of equipment with which the signal generator is most likely to be employed.
Signal generators for use in the a-m broadcast band, for instance, are provided with ampli-
tude modulation, and those for use hi testing f-m receivers are frequency modulated. It
is generally desirable to limit the modulation to one type and to provide means of reducing
unwanted types of modulation.
AMPLITUDE MODULATION. Both the impedance-stabilized oscillator and the
electron-coupled oscillator are susceptible to plate modulation with little accompanying
frequency modulation. In the impedance-stabilized oscillator, the frequency is inde-
pendent of applied plate
voltage over a wide range
if the proper value of sta-
bilizing impedance is
used. Since signal gener-
ator oscillators are tuned
over wide frequency
ranges, however, it is nec-
essary to track the stabi-
lizing impedance with the
main frequency control if
satisfactory performance
is to be obtained. In the Hartley oscillator, the stabilizing impedance is a condenser for
both the grid and plate stabilization types, and this condenser must be kept proportional
to the total value of tuning condenser as the latter is varied. Figure 8 is a diagram showing
this type of oscillator with plate modulation.
The audio power output from the modulator tube must be about 3 times the r-f power
from the oscillator if 100 per cent modulation is to be obtained. This can be accomplished
by means of a voltage dropping resistor between the plates of the r-f and modulator tubes
having a value such that the plate potential of the r-f tube is about 70 per cent that of the
modulator. This resistor must be adequately bypassed for the lowest audio frequency
employed. The time constant of the self-biasing circuit in the grid of the r-f oscillator
must be such as to be able to follow the highest modulation frequency if the same peak
audio voltage is to provide the same percentage modulation of the carrier.
The electron-coupled oscillator circuit depends for its frequency stability on the main-
taining of a fixed ratio for plate and screen voltages. This is best accomplished by feeding
the screen from a voltage divider between plate and ground of sufficiently low resistance
that the screen voltage is in-
/ Audio bypass
condenser
ttage dropping resistor
Voltage dropping
resistor
FIG. 8. Modulation of Impedance Stabilized Oscillator
lodulator
Direct Coupled Modulation of Electron Coupled Oscil-
lator
variant with screen current.
The screen must be bypassed
with a condenser having low
impedance to the r-f voltage
but high impedance to the
modulating voltage. As in the
impedance-stabilized oscillator,
a dropping resistance must be
employed between the plates of
the r-f and modulator tubes if
100 per cent modulation is to
be obtained. A possible varia-
tion, of course, is to supply the
tubes from different taps on a power supply and to couple the modulator to the r-f oscillator
by means of a transformer. A circuit diagram illustrating the former scheme is shown in
Pig. 9, and the latter alternative is shown in Fig. 10. This eliminates the need of a dropping
11-94
ELECTRICAL MEASUREMENTS
R-f chcfee
resistor but requires a tapped power supply voltage and a transformer of flat response
over the audio band width used. Where extreme freedom from f-m effects is desired, an
r-f amplifier is modulated rather than the r-f oscillator. Under these conditions, the
r-f oscillator works at constant potential and is lightly loaded. This arrangement also
makes the oscillator frequency stable with changes in loading of the output attenuator.
The only disadvantage of the scheme is concerned with the necessity for providing a tuned
amplifier which is ganged with the r-f oscillator. The increase in stability obtained,
however, is sufficiently great to
Modulation warrant the use of this method
with signal generators of the
precision type.
Most signal generators for use
in testing broadcast receivers
are equipped with means of
modulating at 400 cycles, this
frequency having been stand-
ardized for receiver testing.
Usually, provision is also made
for modulation by means of an
external oscillator operating at
any desired frequency in the
+200 +300
FIG. 10. Transformer Coupled Modulation of Electron Coupled
Oscillator
audio range. If suitable precautions have been taken in choosing the time constants of
the grid leak and condenser biasing system and of the plate dropping networks, per cent
modulation may be calculated by impressing various d-c voltages on the plate of the r-f
oscillator and measuring the variation in r-f output by means of a vacuum-tube voltmeter
or other method. A meter which measures the impressed audio voltage may then be
calibrated in terms of per cent modulation. Various types of a-c meters have been used
for this purpose such as thermocouple, vacuum-tube voltmeter, and rectifier-type meters.
Xf other than sine wave modulation is externally applied, the indication of such meters
must be corrected accordingly.
FREQUENCY MODULATION. For use in visual alignment of wide-band filters as
well as for testing frequency-modulation receivers, a frequency-modulation generator is
often required. Several methods for varying the radio frequency at an audio rate have
been employed. The simplest of these consists of a rotating trimmer condenser, in parallel
with the oscillator tank, mounted on the shaft of a small motor. This scheme allows wide
frequency variation. It suffers, however, from several defects, among them being troubles
encountered from vibration,, contact troubles if slip rings are used for connection, variation
in amount of frequency swing as the center frequency is varied, and production of undesired
amplitude modulation. The audio waveform and frequency of such a device are usually
fixed. A similar scheme makes use of a vibrating rather than a rotating plate. This
allows modulation at higher audio frequencies and the frequency may be more readily
varied. The obtainable frequency sweep is much smaller, however, and a frequency
multiplier scheme must usually be employed to obtain the required sweep in the r-f output
frequency.
A method which is more complex but considerably more versatile makes use of a react-
ance tube modulator. The frequency modulation obtainable with this method without
large accompanying amplitude modulation is small, and a frequency multiplier scheme
must be employed. To eliminate the necessity of tuning the multiplier stages, a heterodyne,
system such as that shown in Fig. 1 1 is usually employed.
Fbced r-f
oscillator
Frequency
Mi
Amplitude
limiter
Output to
attenuator
multiplier
Reactance
modulator
Var
r-f osc
able I
:iJlator|
Desired
audio waveform
FIG. 11.
Constant Deviation Frequency Modulator
With such a system, the frequency swing of the output frequency is independent of the-
center frequency. A typical generator of this type produces a frequency swing of over a
megacycle per second at center frequencies from 60 to 120 megacycles per second.
At microwave frequencies, where velocity modulation tubes are usually employed,
frequency modulation can readily be accomplished by applying the modulation signal to-
MODULATION OF SIGNAL GENERATOKS
11-95
the reflector of a reflex-type oscillator. At 3000 megacycles per second, for example, a
frequency swing of approximately 30 megacycles per second can be obtained with accom-
panying amplitude modulation of approximately 50 per cent. Frequency swings of 4 or 5
megacycles per second can be obtained with negligible amplitude modulation.
, PULSE MODULATION. For testing radar, blind landing, and similar systems, pulse-
modulated generators are required.
Systems using pulse modulation are usually located in the ultra-high-frequency or
microwave portions of the spectrum, so that this type of signal generator is most commonly
found in these frequency ranges. Requirements for pulse modulation vary widely ._ A
versatile type of instrument which has great usefulness provides a pulse of variable width
and of variable delay from an initiating trigger pulse. Figure 12 shows such a pulse
modulator designed to operate with a velocity variation oscillator. The circuit is designed
11-96 ELECTRICAL MEASUREMENTS
to operate either with an external trigger voltage applied at the SYNC IN jack (J-101) or
with its own synchronizing signal developed by the PRF oscillator. In the latter case the
forward edge of the square pulse produced by the PRF multivibrator V-103 is differentiated
in the grid circuit of the output synchronizing trigger amplifier V-104 so as to produce a
short pulse in the output of this tube. This pulse is then fed to a cathode follower output
stage which delivers a positive synchronizing trigger from J-102. The output of either
the external synchronizing pulse or the self-generated synchronizing pulse is selected by
switch S103-A and fed to the delay multivibrator V-106. The trailing edge of the pulse
produced in this multivibrator is differentiated in the grid circuit of the pulse amplifier
tube V-107. The negative pulse so produced drives V-107 far below cutoff, and the time
required to reach the conducting state again is determined by the time constant of the
differentiating circuit in the grid of the pulse amplifier stage. This pulse is then squared
and amplified in V-108, V-109, and V-110, and delivered to the keyer V-lll and V-112.
The cathode return of the keyer tube is connected to the normal reflector supply voltage
for the velocity variation tube, which may be adjusted to the correct value for proper
operation of the tube when the M OD-CW switch is in the CW position. With the switch
then thrown to the MOD position, and in the absence of a pulse, the reflector potential is
such as to preclude oscillation. During the pulse, however, the reflector voltage is restored
momentarily to its previous value. Pulsed operation of the velocity variation tube is
thus achieved. The circuit is designed to operate with pulse recurrence rates from 50 to
5000 pps with pulses delayed from the trigger pulse from 1 microsecond to 100 micro-
seconds, and having widths variable from 0.5 to 30 microseconds.
In using such pulse modulation systems, care must be exercised in assuring that the Q
of the r-f circuit being modulated is sufficiently low to pass the sidebands generated by
the pulse operation. For r-f frequencies below 100 megacycles per second this requirement
is difficult to meet if stable oscillator performance is to be obtained. A method which is
reasonably successful consists in pulsing an r-f amplifier driven by the oscillator. The main
problem encountered here is to provide sufficient shielding so that no r-f output is present
between pulses. The degree of shielding required is very great if it is desired to test
sensitive receivers, and it is difficult to obtain largely because of coupling due to internal
electrode capacitances of the amplifier tube. A second method consists of pulse-modulating
a higher-frequency oscillator and obtaining the desired frequency by heterodyne methods.
The problem in applying this technique is largely that of filtering out the undesired fre-
quency components in the output.
38. STANDARDIZATION OF OUTPUT POWER
One of the most difficult problems in signal generator design is to determine the r-f
power output accurately. One method that has seen considerable application in the lower-
frequency ranges is to measure the current into a resistive output attenuator by means of a
thermocouple. The quantity of interest is, of course, the output voltage (or power) into
a specified load impedance. It is desired, then, to have the thermocouple read the voltage
(or power) at the input to the attenuator so that, the attenuator having been calibrated,
the output voltage (or power) will be known accurately for all settings of the attenuator.
Several considerations enter into the validity of such a calibration.
In order that a given thermocouple reading will correspond to a given voltage or power
level at the input to the attenuator, the impedance seen looking into the attenuator from
the thermocouple must remain constant for all attenuator settings, assuming that the
attenuator output is correctly terminated. At frequencies low enough so that the at-
tenuator elements can be considered pure resistances, this condition can be met (see
article 39). Difficulty is encountered at the higher frequencies, however, in that the
attenuator input becomes reactive so that its impedance varies with frequency. Under
these conditions the input current no longer bears a fixed relationship to the output volt-
age. At higher frequencies, the thermocouple impedance itself is also subject to variation
due to the impedance presented to the heater by the couple and its associated measuring
leads. The design of an output filter for the couple, which permits a very low capacitive
admittance to ground at the higher frequencies, becomes very difficult.
The difficulty is minimized by using heater wires of very small diameter. Thermocouples
of the separate heater type, where the couple is insulated from the heater by a small glass
bead, minimize these effects. They are, in turn, sluggish in operation and less sensitive
than direct-contact types. Correction must also be made for skin effect of thermocouples
used at high frequencies.
At very high frequencies, where the physical distance between the thermocouple and
tfc* attenuator and between the thermocouple and the signal generator oscillator becomes
STANDARDIZATION OF OUTPUT POWER 11-97
an appreciable part of a wavelength, further trouble is encountered from reflections from
tne couple itself as seen by the signal generator oscillator and variations in the phase of
such reflections as a function of frequency due to changes in the electrical lengths involved
as the frequency changes. For these reasons, thermocouples have seen their greatest
application in the frequency range below 10 megacycles per second although they may be
used with special precautions at very much higher frequencies.
A second method for standardizing output consists in the use of a high-impedance
vacuum-tube voltmeter at the input to the attenuator. It is usually desirable to have the
reading ^of such a vacuum-tube voltmeter independent of modulation. This may be
accomplished by utilizing an averaging type voltmeter circuit. This type of operation is
obtained when the vacuum tube of the vacuum-tube voltmeter is operated with large
voltage input and with grid leak and condenser time constant sufficiently small to allow it
to follow the audio modulation. Under these conditions, the meter reads the average r-f
voltage applied to its terminals. Diode voltmeters with large applied voltage may also
be used; they have the advantage of maintaining calibration with tube life. It should
be remembered that the power output from a modulated oscillator is proportional to
(1-1- m2/2), where ra is the fractional modulation (per cent modulation/ 100), so that m
must be known if it is desired to determine the power delivered to the attenuator (or
effective voltage at the attenuator input).
Vacuum-tube voltmeters may be used at frequencies up to those where transit time
effects reduce the rectification efficiency and thus introduce error. Transit time may be
minimized by close electrode spacing and high applied voltages. Close spacing, however,
introduces large interelectrode capacitance, and this may itself become a source of error.
Interelectrode capacitance may be reduced by making the physical size of the electrodes
small, so that an ideal tube for the purpose would have very gm^l electrodes spaced close
together. In addition, it is necessary to take special precautions to minimize the induct-
ance of the leads to the tube electrodes. In the acorn-tube types lead inductances are
sometimes minimized by bringing out two leads in parallel from each electrode. In tubes
such as the 2C40, heavy cylindrical leads are employed. For acorn-type diodes, the reduc-
tion in rectification efficiency is of the order of 30 per cent at 500 megacycles per second
for voltages of 0.5 volt or less. This effect, together with the change of input impedance
with frequency, limits the range of usefulness of the vacuum-tube voltmeter as a power
output monitor.
The deleterious effects of transit time can be irdnimized to some extent by substituting
a crystal rectifier for a vacuum tube in a voltmeter circuit. A semiconductor such as silicon
in crystalline form is embedded in a conducting material which forms
one contact. The second contact is made through a tungsten whisker.
The resistance between the whisker contact and the semiconductor is
non-linear and may, therefore, be used to rectify an impressed alter-
nating voltage. Though transit time in such a crystal rectifier is
entirely negligible, a similar effect occurs which is due to the capaci-
tance between the whisker contact and the crystal which may be FIG. 13. Equivalent
thought of as shunting the non-linear resistance as shown in Fig. 13. Rectifier Iys
Here, rs represents the resistance of the bulk crystal between the
barrier layer and the fusible metal in which the crystal is embedded, re represents the non-
linear resistance between the whisker and the crystal, and O is the capacitance between the
whisker and the crystal across the barrier layer. At high frequencies, the capacitance
shunts the non-linear resistance in such a way as to reduce the rectification efficiency,
producing an effect similar to that produced by transit time in tube rectifiers. With the
type 1N21-B rectifier, however, this effect is small for frequencies at least as high as
1000 megacycles per second. Other disadvantages to the use of crystals exist, however,
among them non-uniformity of characteristic and variation of impedance among crystals
of the same type, and a change of characteristics with overload.
For very high-frequency applications, the variation of indicated power with frequency
due to variation in electrical length of the leads to the power indicator has led to the use
of systems which divert a known fraction of the power from the signal generator oscillator
to the power indicator. Bolometer elements are frequently used as the power-detecting
devices in such a system (see article 11-33). They are sensitive detectors of r-f power,
having resistance slopes of several thousand ohms per watt. For example, a 10-milHampere
Littlefuse has a slope of 2800 ohms per watt, while a 5-milliampere Littlefuse has a slope
of 5100 ohms per watt. Commercially available Littlefuses are often used as r-f power
detectors and are quite satisfactory up to frequencies of several hundred megacycles per
second. At higher frequencies, their geometry is undesirable and special bolometer ele-
ments such as that shown in Fig. 14 are employed.
The resistance-power curve of a thermistor is not accurately linear as is that of a hot-
11-98
ELECTRICAL MEASUREMENTS
wire bolometer. This is of little importance when it is desired to monitor the r-f power
at constant level but becomes important when it is desired to provide an easily calibrated
indicator which will measure power over some range. The r-f impedance of a bolometer
depends on its geometry as well as on its resistance. It has been found more difficult in
manufacture to hold the r-f impedance of thermistor units than it is with special hot-wire
bolometers.
If it is desired to operate any type of temperature-sensitive power indicator over wide
ranges of ambient temperature, some form of temperature-compensating circuit must be
employed. This problem becomes more acute as the sensitivity of the power indicator is
increased. Temperature-sensitive elements such as those used in the power-measuring
Attenuator
18 gaga
% copper wire
0.0000375'V'
platinum wire
FIG. 14. Hot-wire Bolometer
. Mta* *WV\; | . ^AAr^-VvNVj 1 -O
FIG. 15. Power Monitor Equivalent Circuit
circuit may be employed to accomplish the required compensation. For a direct-reading
bridge circuit, two such compensating elements are, in general, used. One of these main-
tains the zero reading, and the other adjusts the slope of the indicator so as to maintain
the correct calibration.
In the use of power indicators which absorb a fraction of the generator power, care
must be taken to insure that the power split between the power indicator and the output
circuit is maintained constant over the frequency band of operation.
At the lower radio frequencies where line lengths may be neglected this problem does
not present serious difficulties. Here, an arrangement such as that shown in Fig. 15 may
be used where the power-sensitive element is in series with the output attenuator. Here,
if the line length between the power detector zp and the output attenuator za can be
neglected, the current in the two elements is common so that the power ratio is simply
Ta " TJM (3)
where re(zp) represents the real part of the power indicator impedance.
At frequencies high enough so that the line length becomes an appreciable part of a
wavelength, the current is no longer the same in the two elements and the equation holds
only if the impedance of the attenuator is transformed down the line to a point close to zp.
Then, if the impedance of the attenuator is frequency dependent, changes in both the real
and reactive components will affect the power split. The difficulty is overcome only by
maintaining the attenuator imped-
ance close to the characteristic im-
pedance of the line over the fre-
quency range.
At very high frequencies, coaxial
or wave-guide structures are used.
One method of monitoring power
from a cavity-type oscillator is
shown in Fig. 16, Here the power
from the oscillator is coupled through
two openings in the cavity to wave-guide-beyond-cutoff attenuators which feed the power
monitoring and output circuits respectively.
The power delivered to the monitor is then:
2
Power sensitive
element Z
Attenuator matching
fmpedauce ZA
>ass
condenser
Waveguide-beyond-cutoff
attenuators
FIG. 16. Power Monitor for Cavity Oscillator
where Ep = voltage induced in coupling loop feeding the power detector, zp
of power detector, and re(zp) — real part of zp.
Similarly, the power delivered to the attenuator is given by:
(4)
impedance
(5)
where EA = voltage induced in coupling loop feeding the attenuator, ZA - impedance of
attenuator seen looking from the loop, and re(zA) — real part of ZA-
The ratio of these two powers is then given by
?£
EA
X
(6)
ATTENUATOR DESIGN 11-99
Since the ratio EP/EA can be made quite constant over a wide frequency band, if sym-
metrical coupling to the cavity is employed, this reduces to:
(7)
One way to make the right-hand side of this equation constant is to have both zp and
ZA equal the real characteristic impedance of the lines in which they are placed.
A similar situation obtains in wave-guide circuits where the monitor and attenuator are
placed in two arms of a wavelength T and To
are fed from the third arm as shown in bridge * generator
Fig. 17. Here the monitor and attenuator
are effectively in series. The power split eyp
is given by condenser | ^x^ / y* / >• Output
PA re(zA) FIG. 17. Wave-guide Power Monitor
This can also be made constant by matching both attenuator and power indicator to
the wave guide.
39. ATTETTOATOR DESIGN
For frequencies up to about 2 megacycles per second, resistive attenuators using Ayrton
Perry non-inductive wire-wound resistors may be used. In order to maintain the input
and output impedance of such an attenuator con-
stant as the attenuation is varied, iterative net-
works of the T or a- type are used. Such a T
network, designed to match without reflection
the generator impedance rg to a load resistance
FIG. 18. T-type Attenuator TL, is shown in Fig. IS. If the generator and load
are to be connected to the network without intro-
ducing reflection, rin must equal rg and r0ut must equal TL- The attenuation constant of
such a network is denned by
•Bout _ lout _ -a (Q}
-=— — j— — e (V)
-Grin -tin
= ln^ (10)
-C'in jfin
For given generator and load resistances and specified attenuation constant the elements
of the network are given by:
(rt + TL) tank (f J + T, - n (llo)
n _
(TI + TL) tanh { - ) - r, + TL
T2 ^ (116)
(lie)
2sinho:
In the special case where rg = TL = n>, these expressions reduce to:
n = r2 = r0 tanh | (12o)
rs = -rV (126)
sinh a.
The -unsymmetrical case is of interest in signal generators for the broadcast band since
it is sometimes desired to make the output impedance sufficiently low that the voltage
developed across it is independent of the impedance connected to the output terminals.
The attenuation of the network may be varied and constant input and output impedances
maintained if the resistances are kept in the ratio denned by the equations.
In practice, accuracy requirements and difficulty in shielding output from input make
it undesirable to utilize a single T or x section for covering large ranges of attenuation.
11-100
For the* reasons, a
ELECTRICAL MEASUREMENTS
attenuator is commonly employed. A useful form of
19 If K = the ratio by which the voltage across rL
;, the resistances n and r2 are given by :
(13a)
TL (K - 1)
r2 = rz,
(136)
The input resistance rm is independent of the position of the tap switch and is given by:
(U)
where
+ 4r2) +
Between TL and the step attenuator, it is usually desirable to place a variable T pad
attenuator of the type previously described in order to obtain a fine control. TL may be
t^e external load resistance into which the generator is designed to feed, or it may be made
Resistive center conductor
ru Output
FIG. 19. Ladder-type Attenuator with
Constant Input Impedance
V
Resistive disks
FIG. 20.
Coaxial IT Sec-
tion
ResistJve matching transformers
low in value and incorporated into the signal generator in which case the actual load
impedance must be large compared to rL for proper operation. For satisfactory operation,
each section of the attenuator must be separately shielded and a separately shielded low-
capacity switch must be employed. , _ ., . . , ,. .
For high-frequency applications, T or TT sections may be built in coaxial line iorm as
shown in Fig. 20. Units of this type may be used up to the frequency where the length of
line becomes an appreciable part of a wavelength, and
they have seen successful operation up to frequencies as
3 Dielectric high as 1000 megacycles per second. The resistive ele-
ments may conveniently be made of glass rods and disks
coated with thin metallic films. A decade attenuator may
be made by mounting several such elements in a turret
arrangement.
At microwave frequencies, attenuators consisting of
resistive sections of coaxial line equipped with resistive matching transformers have been
successfully employed. A diagram of such a unit is shown in Fig. 21.
The band width of such devices is limited by the change in attenuation with frequency
and by the frequency sensitivity of the resistive matching transformers.
A type of attenuator which has seen increasing use in signal generator applications is
shown in Fig. 22. This type is known as a wave-guide-beyond-cutoff attenuator and makes
Resistive attenuating section
FIG. 21. Microwave Attenuator
•*-L~*
^ ^.<^v^Wv^
t
D
X lA
rpW/////////////V I \
1 I
V
Coupling loops
Loop coupling attenuation = 32.0 ^1 - ( ' 2 ) db Per diameter displacement of loops.
Disk coupling attenuation = 41.8 \1 ~ ( — -« — ) db per diameter displacement of loops.
FIG. 22. Waveguide-beyond-cutoff Attenuator
use of the fact that, for diameters below a critical value which depends on the frequency
and mode of propagation, waves in a hollow tube suffer no phase displacement but are
damped exponentially in amplitude. Inductive coupling between loops and capacitive
coupling between disks in such a hollow tube may be thought of as taking place in this
SHIELDING PROBLEMS 11-101
way. The attenuation in decibels is then linear with displacement and follows the law
given in the figure for the two cases of loop and disk coupling respectively. The loop-
coupled attenuator has the advantage that its rate of attenuation is lower than that of
any other mode and is thus less susceptible to errors due to undesired coupling to other
modes, since these die away more rapidly and become unimportant at any but the lowest
attenuator settings.
At low frequencies, a coil of several turns is usually employed in order to reduce the
minimum insertion loss. For low-frequency applications where the skin depth is appre-
ciable this effect must be taken into account since it modifies the effective diameter. This
may be done by adding 2p to the measured diameter, where p is the skin depth. For
copper, p is given by:
6.6
P = —F X 1CT3 cm (15)
V/
where / = megacycles per second.
The input and^output impedance of this type of attenuator is reactive, and it is necessary
to provide resistive pads to match the generator and load. These pads contribute to the
initial insertion loss, which is of the order of 25 db in practical designs. The high initial
insertion loss limits the use of this type of attenuator, although it is satisfactory for many
signal generator applications where the power level of an oscil-
lator must be reduced to the noise level of a sensitive receiver. vwvv o
The power delivered to a load impedance from any attenuator /J
system can be analyzed in terms of Thevenin's theorem as shown E ^> terminals
in Fig. 23. Here zg is the impedance seen looking into the out-
put terminals and E is the open-circuit voltage measured at these
terminals. At low frequencies, zg is often made small compared ^ J3 A
to the load impedances with which the generator will operate so
that the output voltage is essentially independent of ZL~ A dummy antenna which simu-
lates the impedance of an actual receiving antenna is then placed between the signal
generator terminals and the receiver input.
At higher frequencies, line length between the signal generator and load cause consider-
able difficulty so that a better scheme is to make zt equal to the characteristic impedance
of the line which will be used. The load impedance is then also matched to the line so
that the voltage at the load is E/2. If the receiver to be tested does not present an input
impedance equal to the characteristic impedance of the line, it may be transformed to this
impedance by means of a suitable transformer. If this is not done, an error will be intro-
duced which can be calculated by means of the transmission-Hne equations,
40. SHIELDING PROBLEMS
There is usually a difference in level of the order of 100 db between the signal generator
oscillator power and the attenuator output power when the generator is used for receiver
testing. This makes necessary extreme precautions in the matter of shielding. The depth
of penetration in a metal is defined as that depth to which the electric or magnetic field
falls off to 1/8 of its value at the surface, where e = 2.718. An attenuation of 100 db
requires 11.5 skin depths. At a frequency of 1 megacycle per second, this corresponds to
0.076 cm in copper. Thus, except for very low frequencies, the thickness of the metal
required is determined by mechanical rather than electrical considerations. The real
problem is concerned with the bringing in of d-c leads and control shafts to the oscillator
and with the necessity of providing removable covers for the shield case. Separate shield-
ing boxes should be provided for;the main units in the signal generator such as the oscil-
lator, the power measurer, and the attenuator system. These individual shields are then
enclosed in an overall shield and are preferably grounded to it at a single point to eliminate
circulating currents which can induce voltages in lead filters or other output connections.
Gaskets made of compressed woven metal are useful in preventing leakage from removable
covers.
For low-frequency lead filters, conventional XC-type filters may be used. At higher
frequencies, particular attention must be paid to the condensers used since these may,
in fact, become inductive. Condensers of the button type are particularly useful for this
purpose.
At frequencies above 2000 megacycles per second, lossy filters may be employed to
advantage. A filter consisting of a coaxial line having powdered iron between the con-
ductors represents one such type of filter which has seen considerable application. At
3000 megacycles per second, such a filter, 4 in. in length, can be made to have an attenua-
tion of more than 100 db,
11-102 ELECTRICAL MEASUREMENTS
Control shafts may conveniently be brought into shielded generators by utilizing the
wave-guide-beyond-cutoff principle and employing Bakelite shafts feeding through metal
tubes which are soldered to the shielding box. A tube having an inside diameter of 1/4 in.
will, for instance, have an attenuation of about 100 db for each 3/4 in. of length for frequen-
cies up to 15,000 megacycles per second. Another method of feeding shafts through a
shielded partition is by means of a flexible diaphragm type of coupler which solders to the
shield box and which transforms a nutating motion into a rotary one in a manner which
allows metallic continuity through the coupling.
41. POWER MEASUREMENT
Power measurers are of two types, one which samples the power in a transmission line
between generator and load and which absorbs only a small fraction of the power being
measured, and a second type which absorbs all the power being measured, in general con-
verting it to heat. A vacuum-tube voltmeter of impedance high compared to the generator
or load is an example of the former type; a bolometer or crystal power measurer terminating
a transmission line is an example of the latter type.
All the types of power measurers discussed under the section on signal generators may
be extended to measure higher powers through the use of attenuators appropriate to the
frequency range involved. Bolometer-type power measures of the hot-wire or thermistor
type are particularly adaptable to this use since they may conveniently be matched into
coaxial lin.es. Again, broad-band designs may be evolved up to frequencies where the
length of the bolometer element becomes an appreciable part of a wavelength. By means
of special matching techniques, broad-band designs have been made up to frequencies of
10,000 megacycles per second.
Attenuators of resistive center conductor coaxial line using the thin metallic film on
glass techniques can measure powers as great as a few watts. For higher power, lossy
attenuators which can be matched over a considerable frequency range can be made by
filling the space between conductors in a coaxial line with a lossy compound such as may
be made with graphite or iron powder and a suitable cement binder. With proper propor-
tions of lossy material to binder the loss per unit length can be adjusted to permit the power
absorbed to be radiated adequately from the length of line used.
BIBLIOGRAPHY
Terman, F. E., Radio Engineering, McGraw-Hill Book Co., 1938.
Terman, F. E., Measurements in Radio Engineering, McGraw-Hill Book Co., 1939.
Sarbacher, R. I., and Edson, W. A., Hyper and Ultra-high Frequency Engineering, John Wiley and Sons,
McArthur, E. D., and Spitzer, E. E., Vacuum Tubes as High Frequency Oscillators, Proc. I.R.E., Vol.
19, No. 11, 1971 (November 1931).
Seeley, S. W., and Anderson, E. I., U.H.F. Oscillator Frequency Stability, R.C.A. Rev., Vol. 5, 77
(July 1940).
Harrison, A. E., Klystron Technical Manual, Sperry Gyroscope Co., 1944.
Karplus, E., The Butterfly Circuit, General Radio Experimenter, Vol. 19, No. 5 (October 1944).
Mayer, H. F., Visual Alignment Generator, Electronics, Vol. 13, No. 4, 39 (April 1940).
Crosley, M. G., Reactance Tube Frequency Modulator, Q.S.T., June, 1940.
Sheaffer, C. F., Frequency Modulator, Proc. I.R.E., Vol. 28, No. 2, 66 (February 1940).
Peterson, A., Vacuum Tube and Crystal Rectifiers as Galvanometers and Voltmeters at Ultra-high
Frequencies, General Radio Experimeter, Vol. 19, No. 12 (May 1945).
Becker, J. A., Green, C. B., and Pearson, G. L., Properties and Uses of Thermistors — Thermally Sensi-
tive Resistors, Electrical Engineering, Vol. 65, No. 11, Transactions, p. 711 (November 1946).
Smith, M. T., An Improved Ultra-high Frequency Signal Generator, General Radio Experimenter, Vol.
15, No. 8 (February 1941).
Scott, H. H., Progress in Signal Generator Design, General Radio Experimenter, Vol. 17, No. 6
(November 1942).
Harnett, D. E., and Case, N. P., The Design and Testing of Multirange Receivers, Proc. I.R.E., Vol.
23, No. 6, 578 (June 1935).
McElroy, P. K., Designing Resistive Attenuating Networks, Proc, I.R.E., Vol. 28, No. 2, 66 (February
Peterson, A., Output Systems of Signal Generators, General Radio Experimenter, Vol. 21, No. 1 (June
Shive, S. L.f Effectiveness of Conduit as R.F. Shielding, Electronics, Vol. 19, No. 2, 160 (February 1946).
SECTION 12
ACOUSTICS
THE SENSE OF HEARING
By JOHN C. STEINBERG AND
^T. W. A. MXJNSON PAGE
1. Description of the Ear 02
2. Sensitivity of the Ear 05
3. Differential Sensitivity 09
4. Masking Effects of Sounds 11
5. Loudness of Sounds 11
6. The Pitch of Steady Sounds 16
7. Localization of Sounds 18
SPEECH AND MUSIC
BY JOHN C. STEINBERG AND W. A. MTJNSON
8. Description of Speech Organs 19
9. Production of Speech 19
10. Speech Power 22
11. Powers Produced by Musical Instru-
ments 24
12. Tests of Speech and Music Transmission 27
EFFECTS OF DISTORTION ON SPEECH
AND MUSIC
BY JOHN C. STEINBERG AND W. A. MTJNSON
13. Effect of Frequency Distortion 30
14. Articulation Tests 31
15. Auditory Perspective 39
ACOUSTIC PROPERTIES OF ROOMS
By VEEN O. KNTJDSEN
16. Requirements for Good Acoustics 40
17. Geometric and Wave Acoustics 41
AET. PAGE
IS. Growth and Decay of Sound in Rooms
— General Considerations 42
19. Reverberation Equations 43
20. Room Resonance 45
21. Reverberation at Different Frequencies. 47
22. The Measurement of Reverberation and
Absorption Coefficients 48
23. Coefficients of Sound Absorption 50
24. Practical Considerations of Sound-ab-
sorptive Materials 57
SOUND INSULATION
BY VEBN O. EJSFUDSEN
25. Noise Measurements 57
26. Acceptable Noise Levels in Different
Buildings 58
27. Fundamental Principles of Sound Insu-
lation 60
28. Coefficients of Sound Transmission 64
29. Practical Considerations in the Selection
of Materials and Types of Structure
for Insulation in Buildings 67
30. Calculation of Insulation in Building
Design 69
ACOUSTIC DESIGN OF AUDITORIUMS
BY VEBN O. KNTJDSEN
31. The Hearing of Speech in Auditoriums. 69
32. Music Rooms 74
33. Practical Procedure for Obtaining Good
Acoustics in Buildings 76
12-01
ACOUSTICS
THE SENSE OF HEARING
By John C. Steinberg and W. A. Munson
In the design of sound transmission and reproduction systems, consideration should be
given to the physical and physiological properties of the voice and ear, and to the charac-
teristics and psychophysiological effect of the different types of sounds that the systems
•are called upon to transmit and reproduce.
1. DESCRIPTION OF THE EAR
The hearing mechanism is usually divided into three parts, the outer ear, the middle ear,
and the inner ear. A cross-section of the ear is shown schematically in Fig. 1.
PIG. 1. Semi-schematic Section of Left Ear. P, pinna; E, ear canal; D, eardrum; A, auditory ossicles;
window; U, Eustachlan tube; S, semicircular canal; N, auditory nerve;
C, cochlea.
O, oval window; R, round wind
THE OUTER EAR. The ear canal (E) has a length of about 2.5 cm, a volume of
1,0 cu cm, and an area at the opening of 0.3 to 0.5 sq cm. The eardrum (D), stretched
across the inner end of the canal, has a horizontal diameter of 1.0 cm, a vertical diameter
of 0.8 cm, and an area of 0.6 sq cm. All these dimensions vary somewhat for different
individuals.
THE MIDDLE EAR. The middle ear is separated from the outer ear canal by the
eardrum. Motion of the eardrum is transmitted across the middle-ear cavity to the inner
ear by means of a system of levers (A) called the auditory ossicles. The ossicles consist
of three small bones, the malleus (hammer) , attached to the eardrum, the stapes (stirrup) ,
attached to the oval window '0) of the inner ear, and the incus (anvil) , which is the con-
necting link between the malleus and stapes. The weights of the three bones are : hammer,
O.023 gram; anvil, 0.025 gram; and stirrup, 0.003 gram. The middle-ear cavity is normally
filled with ah* maintained at atmospheric pressure by virtue of the Eustachian tube (IT)
-which leads to the back part of the throat.
12-02
DESCRIPTION OF THE EAR
12-03
THE INNER EAR. The inner ear, which serves a dual purpose, is a complex labyrinth
of liquid-tilled passageways imbedded in the temporal bone adjacent to the middle-ear
cavity. There-are three semicircular canals, oriented so as to lie in three mutually per-
pendicular planes, and these ducts contain the nerve endings concerned with the mainte-
nance of body equilibrium. Only one canal (5) is shown in Fig. 1. The cochlea (O is a
spiral duct containing the auditory nerve endings. In Fig. 1, it has been drawn on an
enlarged scale relative to the middle and outer ears, and the bone in which the cochlea is
imbedded is not shown. The mean diameter of a semicircular canal is about 1.0 cm. The
cochlear spiral has a mean diameter of about 0.6 cm for the large turn at the base. As
may be seen in the sectional view of Fig. 2, the cochlea is divided by flexible membranes
into three canals, scala vestibuli (7), scala media (J/), and scala tympani (T).
The auditory nerve fibers running between the cochlea and the brain number about
29,000 They terminate with complex interconnections along the basilar membrane (B),
FIG. 2. Semi-diagrammatic Section of the Cochlea. (From Gray's Anatomy.) B, basilar membrane;
V, scala vestibuli; M, scala media; T, scala tympani; -V, cochlear nerve; L, lamina spiralis ossea.-
which extends from the bony ledge (L} to the opposite wall of the cochlea, separating
scala tympani and scala media. The nerve endings are associated with tiny hair cells
which protrude into the liquid filling the small triangular scala media. Scala vestibuli
and scala tympani are interconnected at the apex of the spiral by a small opening called
the helicotrema. At the base of the spiral, scala tympani opens into the middle-ear cavity
through the round window (#), shown in Fig. 1, but the liquid content is retained by a
flexible membrane stretched across the opening. The oval window (0), between the
middle ear and scala vestibuli, is closed by the foot of the stapes and connecting ligaments-
Excitation of the Auditory Nerves. A sound wave in the outer ear canal produces
motion of the eardrum and associated ossicles which, in turn, agitate the liquid in scala
vestibuli through the oval window. When the stimulus is a pure tone at a low level, this
results in an excitation of a small number of the nerve endings enclosed by the adjacent
scala media. When the frequency of the tone is changed, the excitation moves along the
basilar membrane, engaging a different set of nerve endings. In this way the ear differ-
entiates between tones of different pitch. When the intensity of the tone is increased, the
excitation spreads out, and additional nerve endings are stimulated, but those comprising
the initial group probably receive the maximum stimulation. The positions of the stimu-
lation maxima are shown in Fig. 3 as a function of frequency.
At low frequencies the stimulation maxima are very broad and the positions are poorly
defined. It may be that the pitch of low-frequency tones is sensed by the stimulation
frequency as well as by its position.
NERVE CONDUCTION. Physiological research indicates that a nerve conducts on
an "all-or-none" basis. The magnitude of the nerve impulse and the rate of propagation
are independent of the manner of excitation. After an impulse has been transmitted by
a nerve, it must recover its conducting properties before it is capable of being excited
again. This recovery period lasts for a time interval of 1 to 3 milliseconds and varies
12-04
ACOUSTICS
somewhat with the intensity of the stimulus. Thus a nerve fiber is unable to transmit the
wave form of tne exciting
stimulus. Excitation of the
auditory nerves and conduc-
tion of neural pulses to the
brain have been studied by
placing a small electrode on a
single auditory nerve tract of
anesthetized animals and re-
cording the potential gener-
ated. It was found that in-
creasing the intensity of a
,
10,000
8
X
X
6
4
(^
X^
/
f
~
$1000
Z S
/
/
t 6
/
<§ 4
/
r
JE
/I
/
| 2
1
g" 100
£ s
/
6
4
o
10
0
/
\
s
i
2
1
6
2
D
2
4
2
8
pure tone increases the rate
at which pulses are trans-
mitted. Typical results are
shown in Fig. 4. Since a max-
imum rate is attained when
the sound level is increased
about 50 db, other fibers must
be involved in covering the
full intensity range of the ear.
It is believed that the loud-
ness of a sound is related to
the rate at which neural im-
pulses reach the brain from
all portions of the basilar
membrane.
ACOUSTIC IMPEDANCE
OF THE EAR. The acous-
tic impedance which an ear
presents to a telephone re-
ceiver has been measured at
Distance from Hellcotrema In MM
FIG. 3. Relation between Frequency of a Tone and the Position
of Nerve Endings on the Basilar Membrane Which Receive
Maximum Stimulation. (Steinberg.)
the aperture of a receiver cap. The results depend to a large extent upon the way the
cap fits the ear. Typical values are shown in Fig. 5 for the case when the cap is sealed to
the ear and for the case when an air
leak is present between the cap and the
ear. These data are useful in receiver
design, and Inglis, Gray, and Jenkins
describe an artificial ear which they
use for the measurement of telephone
receivers. It consists of a conduit hav-
ing the approximate dimensions and
impedance of a typical ear canal over
the important frequency range. The
exposed end of the conduit is fitted
with a tapered rubber seating surface
on which the receiver is placed. The
other end of the conduit is terminated
by an acoustic network and by the
diaphragm of a small condenser trans-
mitter. The pressures developed at
the transmitter diaphragm for a given
voltage on a receiver placed on the
artificial ear are closely equal to the
pressures that would be produced by
the receiver at the drum of a typical
human ear.
NATURAL FREQUENCY AND
DAMPING CONSTANT OF THE
EAR. The work of Bek&sy indicates
that the frequency with which the
eardrum and ossicles vibrate when
suddenly released from a displaced
position is of the order of 1200 to 1500
10
60
70
cycles. The vibrations decay at a
20 30 40 50
Relative Intensity Level, db
FIG. 4. Relation between Sound Intensity and Nerve
Discharge Rate for a 1050-cycle Tone. (Galambos and
Davis.)
SENSITIVITY OP THE EAR
124)5
rate of 1200 db per sec. Davis and associates' experiments on the electrical response of
the ears of cats indicate a natural frequency from 600 to 1000 cycles and a decay rate of
1000 db per sec. Their work also indicates that the time lag between the sudden applica-
tion of a sound wave on the eardrum and the transmission of the impulse along the auditory
nerve is of the order of 2 to 3 milliseconds. On the other hand, the sensory build-up time,
e.g., the time needed for a suddenly applied steady wave to build up to a steady loudness,
is of the order of 0.2 to 0.25 sec.
200
150
1
|
dance In Acoustic Ohms
L .
3 Ol Ol O
DOOOO
1
^
7 V
/ i
\
--
/•/
"-^
J.
^
"^^
^
3
•^
^*&
^-—
v
S
^
^
*s
E.
JE
—150
—200
i°50
/
/
/
'\
/
/
1. Re
2. Re
Distance of Typical Male Human Ear, Sealed,
actance of Typical Male Human Ear, Sealed,
slstance of Typical Male Human Ear, wlfh Leafc
actance of Typical Male Human Ear, with Leafc
—300
1(
3. Re
4. Re
DO 500 1000 5CX
Frequency In Cycles pej Second
FlG. 5. Acoustic Impedance of Ears as Viewed through Aperture of Receiver Cap. (Inglis,
and Jenkins.)
2. SENSITIVITY OF THE EAR
Ear sensitivity is concerned with the least intense sound that can be heard. Such a
sound is said to be at the "threshold of hearing." Two classes of ear-sensitivity deter-
minations have been reported, "minimum audible pressure" (M.A.P.) and "minimum
audible field" (M.A.F.). M.A.P. is the just-audible sound pressure measured near the
observer's eardrum. M.A.F. is the free field sound intensity of a plane progressive wave
that is just audible to an observer facing the source and listening binauraily: The sound
intensity is measured before the observer's head is inserted in the field. It is convenient
to express minimum audible values in decibels from an arbitrary reference. Reference
intensity has been chosen as 10~16 watt per square centimeter. Corresponding reference
pressure at 20 deg cent and 76 cm of Hg is 2 X 10 ~4 dyne per square centimeter. In-
tensity and pressure levels are the number of decibels from the above references, respec-
tively. Table 1 gives minimum audible values derived by Sivian and White from their
own work and that of others when a small selected group of observers with excellent hear-
ing is used.
Owing to the diffraction effect of the head and to the difference between one-ear and
two-ear listening, it would be expected that M.A.P. and M.AJT. would differ considerably
at high frequencies but not at low frequencies. Various possible causes of the differences
shown in Table 1 at the low frequencies are discussed by Sivian and White, with the con-
clusion that, at the present time, a satisfactory explanation is not evident.
12-06
ACOUSTICS
Table 1* Monaural Minimum Audible Pressure Levels in the Ear Canal and Binaural
Minimum Audible Sound Field Intensity Levels
Frequency
60
100
200
500
1,000
2,000
5,000
10,000
15,000
M.A.P., db
(Monaural) . . .
M.A.F., db
(BiriAiirp.1) . , , ,
59
45
46
33
29
19
14
8
8
3
5
-6
12
_3
26
11
44
22
BINAURAL VS. MONAURAL. Minimum audible values obtained with observers
listening binaurally (two ears) are smaller on the average than those obtained with ob-
servers listening monaurally (one ear). According to Fletcher and Munson, the differ-
ence appears to be accounted for by inequalities in the sensitivities of the two ears of an
observer. They report that the binaural sensitivity is practically equal to that of the
better ear, and that monaural sensitivity is equal to that obtained by averaging the sensi-
tivities of both ears. Figure 6 gives the differences between the sensitivity of the better
Acuity Difference, db
^0 to 4*. en to a
'
^
c
->{'
n
^
."
'
1
>
0 50
100 200 500 1000 2000 5000 10000 20000
Frequency In Cycles per Second
FIG. 6. Difference between tne Sensitivity of the Better Ear and the Average of Both Ears. (Fletcher
and Munson.)
ear and the average of both ears, based on the audiograms of 80 persons of normal hearing.
It gives a means of converting binaural M.A.F. into monaural M.A.F.
VARIATION WITH DIRECTION. The values of M.A.F. given in Table 1 are for
an observer facing the source, i.e., for a progressive wave whose wave front is vertical and
whose direction is normal to a line joining the observers ears. Owing to diffraction effects
of the head, the ear is directive and generally hears best when the open ear is turned toward
the source. The directivity of hearing as reported by Sivian and White is given in Fig. 7.
Directivity is expressed as the variation in monaural M.A.F. with the azimuth of the
vertical wave front: 0° corresponds to the observer facing the source; +90° corresponds to
the open ear toward the source. The variation is expressed in decibels from the M.A.F.
at 0°. A positive value of directivity for any angle means that the ear is more sensitive
at that angle than at 0°. By means of the directivity data, Sivian and White have com-
puted the sensitivity of the ear for the case when an observer is exposed to a diffuse sound
field, such that sound waves of equal amplitudes and random phase angles are equally
probable from all angles. Their results are shown in Table 2.
Table 2. Binaural Mini -mum Audible Sound Field (Random Horizontal Incidence).
(Sivian and WMte)
Frequency
60
100
200
500
1,000
2,000
5,000
10,000
15,000
Binaural M.A.F. T db
(random horizontal in-
cidence)
45
33
19
6
-1
-7
_7
2
18
POSSIBLE LOWER LIMITS OF SENSITIVITY. On certain assumptions, Sivian
and White calculate that the intensity level of thermal-acoustic noise, i.e., noise originat-
ing from the thermal velocities of air molecules, has a value of 11 db below 10 ~16 watt for
a frequency band from 1000 to 6000 cycles, and hence is of the order of the maximum ear
sensitivity. Although the authors regard the calculation as very approximate, it suggests
that the limit of sensitivity may be set by the transmitting medium. If this is so, man
may have maximum sensitivities comparable with those of animals.
EAR SENSITIVITY OF THE POPULATION. The values of ear sensitivity shown
in TaHe 1 are for a selected group of young people with excellent hearing; not all people
SENSITIVITY OF THE EAR
12-07
hear this well. During the New York and San Francisco World Fairs in 1939, which were
attended by people from all parts of the country, a survey of hearing was made in a large
group of the United States population. The results, which are plotted in Fig. 8, show the
percentages of thresholds measured which were above the levels shown by the contour lines,
inus tne data show the percentage of people in the population within the age range
irom 1U to 59 years who cannot hear tones below the levels indicated by the contours.
10
\
—ISO
22,00-oj
—120
-60
500^
300 r
6O
120
180
0
Degrees
FIG. 7a. Increase of Monaural Acuity in a Free Sound Field When the Direction Which the Observer
Faces Is Changed
20
15
XO
5
1°
O
-5
-ao
—180
7600
10,OOC
\5000x»
\
\/
—120
-60
60
120
180
0
Degrees
FIG. 76. Increase of Monaural Acuity in a Free Sound Field When the Direction Which the Observer
Faces Is Changed
For instance, 25 per cent of the population cannot hear a 1000-cycle tone if the intensity
is below the 20-db level (zero = 10 ~16 watt per sq cm). The dotted portions represent
extrapolations of the distributions beyond the intensity and frequency ranges used in the
tests and are, of course, speculative.
VARIATION WITH AGE. Further analysis of the data revealed a progressive dete-
rioration of hearing with age for the average individual, particularly at the higher fre-
quencies. The hearing loss is somewhat greater for men than for women, as shown by
the curves in Fig. 9. For this plot "zero hearing loss" refers to an ear sensitivity equal to
the median value for the population, tested. The contour marked "50 per cent" in Fig. 8
shows the median values as a function of frequency. When the hearing loss exceeds about
25 db at all frequencies lower than 2000 cycles, a person will experience difficulty at times
in understanding speech in classrooms, auditoriums, churches, and similar environments
where the speech level is not very high. A hearing loss of 45 db for frequencies below
2000 cycles results in some difficulty in understanding speech at distances greater than.
12-08
ACOUSTICS
140
?120
100
80
60
40
.£ 0
\
—20
\
\
Feeling
Percent
1
20 50 100 200 500 1000 2000 5000 10,000 20,000
Frequency In Cycles per Second
FIG. 8. Contour Lines Showing the Lower Limit of the Sensitivity for a Given Percentage of Tests
in the Age Group 10-59. (Steinberg, Montgomery, and Gardner.)
30
880 1760 3520
Frequency In Cycles per Second
7040
FIG. 9. Average Hearing Loss for Men and Women in Three Age Groups. (Steinberg, Montgomery
and Gardner.) '
DIFFERENTIAL SENSITIVITY
12-09
than 25 db and 45 db
(Steinberg, Montgomery, and Gardner)
2 or 3 ft, and considerable benefit is usually derived from the use of a hearing aid. Table
3 shows the prevalence of hearing losses greater than 25 and 45 db among the people
tested.
In the age group from 50 to 59 years, Table 3 shows that 3 or 4 per cent of the popula-
tion have hearing losses exceeding 45 db and, therefore, would experience some difficulty
understanding speech at a distance of 2 or 3 ft. Until the hearing loss exceeds about 65 db,
a person will still be able
to use the telephone with- Table 3. Percentage of Tests with Hearing Losses Greater
out much difficulty.
AUDITORY RANGE.
As the intensity level of a
sound is increased, a value
is reached which causes a
sensation of feeling in ad-
dition to the sensation
of tone. Such intensity
levels may be taken as
practical upper limits of
hearing, and they have
been called the "threshold
of feeling." The observed
data on the threshold of
feeling were the number
of decibels between the
hearing and feeling thresh-
olds for pure tones and
were obtained by means
of telephone receivers held
to the ear. The absolute
threshold of f eeling plotted
in Fig. 8 was obtained by
adding the observed data to the lower limit of audibility shown in Fig. 8. The lower
limit is the M.A.F. determination of Table 1.
The lower limit and the feeling curve have been extrapolated until they meet, thus
forming an enclosure called the "auditory sensation area." This area has the property
that any sinusoidal sound wave having a frequency and an intensity level within the area
will cause a sensation of tone. The dashed portions of the curves serve as a means of
defining the upper and lower frequency limits, i.e., the lowest and the highest frequency
that can be sensed as a tone. Measurements have been made using frequencies varying
from about 8 to 40 cycles for the lower limit and from 12,000 to 35T000 cycles for the upper
limit, but, for the most part, very little attention was given by the experimenters to the
intensity levels at which the determinations were made. In drawing in the dashed curves,
consideration was given to available data on frequency limits, and values of 20 cycles and
20,000 cycles were selected for the lower and upper frequency limits, respectively. These
limits were taken as more or less typical for persons of normal hearing in the age range
from 18 to 23 years but do not represent the extreme values found in exceptional cases.
Age Group
25-dbLoss
45-dbLoss
Frequency
Frequency
880
1760
3520
7040
880
1760
3520
10-19
Men
1.7
1.8
1.1
1.8
1.8
3.5
5.5
7
9.5
13
1.6
1.2
1.2
1.6
3.5
3.5
9.5
7
17
14
4.5
1.2
7
2.2
15
5.5
32
11
48
22
8
2.5
9.5
3.5
19
10
39
24
58
43
0.6
0.6
O.I
0.4
0.3
1.2
1.4
2.1
2.6
4
0.6
0.4
0.3
0.3
0.6
0.8
2.6
1.5
6
3
1.8
0.3
2.7
0.7
6
1.6
16
3
27
7
Women .
20-29
Men
Women . .
30-39
Men
Women
40-49
Men
Women ....
50-59
Men
Women ,
3. DIFFERENTIAL SENSITIVITY
The differential sensitivity of hearing refers to some aspect of the smallest change of a
stimulus that can be detected. Available data on the subject are confined almost entirely
to measurements of the minimum perceptible increments of frequency and of intensity
when the stimulus is a single-frequency tone. The values obtained depend to some extent
upon the method of measurement, probably because the just perceptible change (differ-
ence limen) is affected by the rate at which the change is made as well as other variables
common to tests of this type. Until a measuring technique is standardized, the data shown
should be regarded as of the exploratory type. In Fig. 10 the results of extensive measure-
ments of A/T the difference limen for frequency, are plotted. For levels greater than 40 db
above threshold, and for frequencies greater than 500 cycles, the frequency D.L. has the
approximately constant value of 0.3 per cent.
These results were obtained by listening to the tones with head receivers. When the
measurements are made by listening to a loudspeaker in a room, much smaller values
can be observed. In this case the change in frequency is detected by intensity changes
due to the shifting of the interference pattern in the room with frequency change. A
12-10
ACOUSTICS
100
1000
10,000
Frequency In Cycles
FIG. 10. The Frequency Difference Limen with Decibels above Threshold as a Parameter. (Shower
and Biddulph.)
similar set of measurements of AI, the minimum perceptible increment of intensity, is
shown in Fig. 11. For convenient use the increment of intensity expressed in decibels,
10 log (I + AJ/I), is plotted as the ordinate. For levels greater than 40 db above thresh-
old, and for frequencies between 200 and 7000 cycles, the intensity D.L. varies from 0.25
to 0.75 db.
10.0
O.I
100
1000
10,000
Frequency in Cycles
It The Intensity Difference Limen with Decibels above Threshold as a Parameter. (Biesz.)
LOUDNESS OF BOUNDS
12-11
4. MASKING EFFECTS OF SOUNDS
When listening to speech or music it often occurs that a disturbing noise interferes to
such an extent that the desired sounds are partially or entirely obliterated. The noise is
said to have a masking effect, and the magnitude of the effect is defined by a "masking
spectrum" of the noise. Measurements of masking spectrums are made by determining the
threshold of audibility of
single-frequency tones in "^ 90
the presence of the noise
and again when the noise
is absent. If 0 is the in-
tensity level of a tone of
frequency /, that is just
audible in the presence of
a noise, and jSQ is the in-
tensity level that is just
audible under quiet listen-
ing conditions, then M,
the masking at the fre-
quency /, is denned by the
equation : M — fi — j8o. A
plot of M as a function of
the frequency of the tones
is called a masking spec-
trum. If the intensity
spectrum of a noise has
been measured by means
of a sound meter and
niters, the masking spec-
trum may be derived by
use of Fig. 12. Here the
iso-masking intensity per
cycle level of noise has
=-30
FIG. 12.
100 500 1000
Frequency In Cycles per Second
Masking Contours for a Steady Noise.
Munson.)
100OO
(Fletcher and
been plotted as a function of frequency with masking as a parameter. The applications of
these data are limited to portions of the noise intensity spectrum that do not exhibit the
abrupt changes with frequency that occur when a prominent single-frequency component
is present or a filter with a sharp cutoff limits the frequency range of the noise.
5. LOUDNESS OF SOUNDS
Loudness is denned as the magnitude of an auditory sensation, and for steady sounds
it is thought to be proportional to the rate at which neural pulses originating along the
basilar membrane arrive at the brain. A scale of auditory magnitudes has been derived
from loudness tests and can be used whenever the loudness level of a sound is known. A
measurement of loudness level consists of a listening test in which the level of a 1000-
cycle reference tone is adjusted until it sounds equally loud to the sound being measured.
Errors in judgment may be large, and a number of observers may be required to obtain a
reliable average result. The equivalent free field intensity level of the equally loud 1000-
cycle tone is, by definition, the loudness level of the unknown sound.
The loudness level of a sound being known, its auditory magnitude is found by referring
to Table 4, which gives the auditory magnitude, or loudness, as a function of the intensity
level of the equally loud 1000-cycle tone. The figures for the intensity level (loudness
level) of the 1000-cycle tone are in decibels relative to 10~16 watt per sq cm, and a level of
40 db results in an auditory magnitude of one sone. Thus, in Table 4, the loudness cor-
responding to a loudness level of 40 db is 1 loudness unit (1 sone = 1000 millisones). In-
creasing the loudness level from 40 db to 49 db gives a listener the impression that the
magnitude has doubled, so a loudness level of 49 db results in a loudness of 2 units. In-
creasing the loudness level from 49 to 58.1 db again doubles the magnitude of the sensation
for the average listener, so a loudness level of 58.1 db produces a loudness of 4 units. The
empirical relationship between loudness and loudness level is shown in Table 4.
Loudness levels are given in steps of 1 db, or 1 "phon," and zero level is 10 16 watt per
sq cm in a free sound field. The term "phon" is generally used as the unit of loudness
level to avoid confusion with intensity levels of sounds other than a 1000-cycle tone. It
12-12
ACOUSTICS
is believed that the loudness of a steady sound depends upon the rate at which neural
pulses reach the brain, and, although no measurements are available to substantiate this
hypothesis, the concept is useful in explaining empirical methods of computing the loud-
ness of complex sounds. It follows from the manner in which the loudness scale was de-
veloped that a 1-sone sound, for example, is equally loud to any other 1-sone^sound, and
four times as loud as a 0.250-sone sound. It is also true that a 1-sone sound will drop to a
Table 4. Loudness (Millisones) vs. Loudness Level (Pkons)
(Fletcher and Munson)
Loudness
Loudness
Level, db
0
1
2
3
4
5
6
7
8
9
0
1.0
1.42
1.95
2.58
3.36
4.32
5.57
7.10
9.00
11.4
10
14.4
18.7
23.3
28.9
35.1
42,2
50.6
60.3
71.6
85.0
20
100
120
142
165
188
214
242
272
307
340
30
380
421
470
522
577
635
700
763
835
915
40
1,000
1,080
1,170
1,260
1,360
1,470
1,590
1,710
1,850
2,000
50
2,150
2,330
2,510
2,710
2,930
3,160
3,410
3,690
3,980
4,300
60
4,640
5,010
5,410
5,840
6,310
6,810
7,360
7,940
8,580
9,260
70
10,000
10,800
11,700
12,600
13,600
14,700
15,900
17,100
18,500
20,000
80
21,500
23,300
25, IQO
27,100
29,300
31,600
34,100
36,900
39,800
43,000
90
46,400
50,100
54,100
58,400
63, 100
68,100
73,600
79,400
85,800
92,600
100
100,000
108,000
117,000
126,000
136,000
147,000
159,000
171,000
185,000
200,000
100
80
half sone if only one ear is used for listening. These simple relations have all been verified
experimentally. A complex sound having two 1-sone components will be equally loud to
a sound of 2 sones if the components excite nerve endings located in different sections of
the basilar membrane and thus contribute 1 sone each, even though they are sounded
simultaneously. This is not likely to be the case when the frequencies of the components
are close together or the levels are high, since many of the same nerve endings are then
used by both components.
EFFECTIVE STIMULATION DENSITY. The response of the auditory nerve endings
is dependent upon the density of stimulation. If the stimulus is localized, the response
will be different, and the loudness sensation will differ, in general, from the loudness
resulting when the stimulus energy is distributed among a large number of nerve endings.
The relationship between
the frequency of the stim-
ulus and the position co-
ordinate (X) of the nerve
endings stimulated is
shown in Fig. 13.
The ordinate of Pig. 13
gives the position of max-
imum stimulation of the
nerve endings, with re-
spect to the total number,
when the stimulus is a
single-frequency tone.
For instance, at 1000
cycles the curve shows
that 31 per cent of the
nerve endings are on one
side of the point of max-
imum stimulation, and 69
per cent are on the other
100
10000 20000
1000
Frequency In Cycles per Second
FIG. 13. Relation between Frequency of the Stimulus and the Position
of Maximum Stimulation. (Fletcher.)
side. The relationship shown can be derived in several different ways on the basis of dif-
ferent assumptions, but it has been verified only in a qualitative sense by actual nerve counts.
To obtain the effective stimulation density as a function of frequency, for a sound with a con-
tinuous energy spectrum, measurements must first be made with a sound meter that will
analyze sound at all frequencies within the audible range. If the analyzer , measures the
intensity (I) in a frequency band A/ cycles wide, then the readings are related to effective
stimulation densities by means of the equation:
Z = 10 log
LOTJDNESS OF SOUNDS
12-13
where /i is the intensity level of a 1-millisone single-frequency tone, and A/i is a frequency
band enclosing a unit group (1 per cent) of the nerve endings. It is seen that Z is the
ratio, in decibels, of the stimulation intensity per unit group of nerve endings to the
intensity required to excite a 1-miUisone response from the nerves. The equation for Z is
usually given in the more convenient form:
Z = B -f- * - ft,
where B is the measured intensity per cycle level of noise [B = 10 log (J//0 A/)], IQ is the
reference intensity of 10~16 watt per sq cm, K is the band width in decibels which includes
a unit nerve group (K = 10 log A/0, and ft, is the intensity level of a tone when the loud-
ness level is zero [&> = 10 log (/i/I0)]. Values of K, B0, and X are shown in Table 5 for use
in computing and plotting the effective stimulation density for the nerve endings as a
function of their position coordinate, X.
Table 5. Values of K, ft, and X
(Fletcher and Munson)
/ 100 200 300 500 700 1,000 2,000 3,000 5,000 7,000 10,000
X 1 4 7 14 21 31 52 64 78 85 92
K 16.5 15.0 15.0 15.0 15.3 16.0 18.6 20.7 23.9 26.1 28.6
j30 37.4 22.9 14.6 5.7 2.0 0.0 -4.5 -8.5 -4.9 4,9 8.8
LOUDNESS COMPUTATION FOR SOUNDS WITH CONTINUOUS ENERGY
SPECTRUMS. The loudness of a c
steady sound is believed to be propor-
tional to the number of nerve pulses
arriving at the brain in unit time
from all parts of the basilar mem-
brane. We may compute the loud-
ness (AO from the expression:
N
/•100
* f *
*/0
NxdX
where NX> the sone density, is a
measure of the number of nerve
pulses originating from a unit group
of nerve endings in unit time, and
X is the position coordinate pre-
viously denned. The equation is
solved by plotting NX as a function
of X and measuring the area under
the curve. Thus the loudness, N1 of
any sound can be computed when the
sone density is known as a function
of X.
The relationship between sone
density (Nx) and the effective stim-
ulation density (Zx) has been inves-
tigated for sounds characterized by a
continuous distribution of energy,
and it is shown in Fig. 14.
It is not applicable to sounds hav-
ing single-frequency components or
sounds in which the value of the
slope, dZ/dX, exceeds the limits
±2 db. In the latter case, masking
measurements are a more reliable
means of obtaining the sone density
(A^x). The masking (M) is defined
by the equation : M — $ — ft,, where
£ is the intensity level of a single-
frequency tone that is just audible
in the presence of a masking sound,
and /?o is the intensity level when
the loudness level is zero. Figure
15 shows the relationship between
«
±'10
.310"
10
jz:
7
-20 -10 0 10 20 30 40 50 60 70 80
Zx. Elective Stimulation
per Unit Nerve Group (db)
FIG. 14. Relation between the Loudness (Nx) per Unit
Nerve Group and the Stimulation (Zx) per Unit Nerve
Group. (Fletcher and Munson.)
12-14
ACOUSTICS
masking and sone density. The masking method of obtaining the sone density is valid
for sounds exhibiting large values of dZ/dX but not for sounds with single-frequency
components. The masking spectrum of a single-frequency tone is not an accurate indica-
tion of its sone density since the phenomenon of beats between the masking tone and the
masked tone changes the conditions under which the masked tone is detected. This re-
sults in low values of masking at frequencies where the highest values would be expected.
10
10
10
z
0 10 20 30 40 50 60 70 80 90 100
Masking, M (db)
FIG. 15. Relation between Loudness Contribution (JVx) per Unit Nerve Group and Masking (Af).
(Fletcher and Munson.)
LOUDNESS OF SOUNDS COMPOSED OF SINGLE-FREQUENCY COMPO-
NENTS. When a sound is a single-frequency tone at a low level, the nerve endings in
a localized region of the basilar membrane are stimulated. As the level is increased, the
stimulation pattern spreads to adjacent nerves, and at high levels a large proportion of
all the nerves may come into use. The region of maximum stimulation probably does not
change much when the level is raised, but secondary maxima appear at harmonic fre-
quencies owing to non-linear distortion in the ear itself. The masking spectrums shown in
Fig. 16 indicate the nature of the change of the stimulation pattern as the level of a tone
is increased.
As explained in the previous section, the regions of maximum stimulation appear as
depressions because of the beats which occur near the fundamental and harmonic fre-
quencies. Measurements of the conditions for best beats have been used to determine the
magnitude of harmonics produced in the ear. Figure 17 shows the equivalent magnitude of
the subjective harmonics for different pressure levels of the applied sound. Taking the
fundamental as the first harmonic, the abscissa gives the number of the harmonic When
LOTJDNESS OF SOUNDS
12-15
plotted in terms of pressure level, the curves are independent of frequency. It is clear
that the stimulation patterns of single-frequency tones are very complex, and it would be
difficult to plot the sone density as a function of X, as was done for sounds with continu-
ous energy spectrums. However, the loud-
ness of any single component
found from the loudness-level
shown in Fig. 18.
may be
contours
100
90
70
800 Cycles
\\.s
80
8888
00 W ID O
w to co •*
Frequency tn Cycles per Second
FIG. 16. Masking Spectrums of a Single-fre-
quency Tone with Level above Threshold as a
Parameter. (Fletcher, Wegel, and Lane.)
g 140
tr
0 130
JS
i
\!
!
c
0.
o 1 2n
t*
\!
N
V : 1
i
1
T3
i"
\r
\i
X
o 110
8.
f
\>
\
X ;
N
XV
.Q
"° on
[
\>
— x
\i 1
\
^^
»
o 9O
I
c or.
f
O
s^
\l\
X
I 80
-a
}
\\
\
k\
\
s
1
r-
-
5 70
o
•= ^«
\\
\
\ s
K
^s
N
- 6O
\\
\
\\
K
1
1 M
g .f.
\
s1
KK
!\
v
l\
D 40
JE
\
,\
1 Sl "
1
\
1^
4,
N
^
0 3O
\
\ \
\
K
\
N
\
o 2°
1 ,A
\
* \
\
\
>,
<
Number of Harmonic
FIG. 17. Magnitude of Subjective Harmonics.
(Fletcher and Graham.)
The ordinate here is the free field intensity level of a pure tone, and each contour line
is marked with a loudness level. For instance, a 200-cyele tone at an intensity level of
60 db from ICT16 watt has a loudness level of 50 db. Turning to Table 4, we see that the
corresponding loudness is 2.150 sones. If a sound has more than one component, the sone
values may be added to obtain the total loudness, provided that the frequencies of tne
120
rtfl 100 =MJV iWU
Frequency in Cycles per Second
FIG. 18. Loudness-level Contours. (Fletcher and Munson.)
components differ enough so that different nerve groups are stimulated. The ,
r^quLd is a complex function of level and frequency and will not be discussed
Some idea of the effect of different separations of components may be obtained from
12-16
ACOUSTICS
Fig. 19, which shows the loudness levels of several 10-eomponent sounds as a function of
the loudness level of each component.
The first sound had a fundamental frequency of 530 cycles and a difference oi 5^0
cycles between components. The others had a fundamental of 1000 cycles and the dif-
ferences indicated. The dotted line shows the loudness levels corresponding to 10 times
the loudness of a single component. For a more extended treatment of the loudness of
sounds with single-frequency components, refer to an article in the October 1933 Journal
of the Acoustical Society of America entitled "Loudness, Its Definition, Measurement and
Calculation," by Fletcher and Munson.
Loudness Level of 10 Components, db ^
Mtow^tncn^ooioo
ooo Ooo ooooo
s//
^/
X
/&
%
/
//,
Y/
/
&
Y'
/*
t
V/
/
I
/
A
/
4
'A
a Frequency Difference — 530
o " " =340
A " " =230
x ,< " =112
. <. " =50
/
•/
-10°
80 90
10 20 30 40 50 60 70
Loudness Level of Single Component, db
FIG. 19. Effect of Separation of Components on the Loudness Levels of Complex Tones. (Fletcher
and Munson.)
6. THE PITCH OF STEADY SOUNDS
The pitch of a steady sound is the position on a musical scale that would be assigned to
it by a listener. If the sound is a single-frequency tone, its pitch depends upon frequency
and, to a slight degree, upon intensity. At loudness levels less than 40 db the pitch de-
pends only upon frequency, and single-frequency tones at a loudness level of 40 db have
been chosen as standards for comparison with sounds of unknown pitch. The results of
pitch comparisons between single-frequency tones at a 40-db loudness level and tones at
higher levels are shown in Fig. 20. The ordinate is the change in frequency, in per cent,
of a tone that is necessary in order that its pitch remain constant as its level is raised.
For example, the curves show that a 100-cycle tone must be lowered 10 per cent when
the loudness level is increased from the standard level to 100 db. This means that a
90-cycle tone at a loudness level of 100 will appear to have the same pitch as a 100-cycle
tone at a loudness level of 40 db. The curves shown in Fig. 20 are based on data at low
frequencies. Similar experiments by Zurmuhl and Stevens indicate that at frequencies
above 2000 cycles there is a small increase in pitch as the level is raised. An observer's
judgment of the pitch of a sound is thought to be related to the position of the stimulated
region on the basilar membrane. In general, a sensation of lower pitch occurs when the
stimulated region shifts towards the helicotrema.
Table 6. Judgments of Half Pitch
(Stevens and Volkmann)
Standard frequency 150 250 500 1,000 2,000 3,000 5,000 10,000
Frequency far half pitch 85 111 206 373 633 1,009 1,437 2,064
THE PITCH OF STEADY SOUNDS
12-17
Experiments have been made to determine how much the frequency of a standard tone
must be shifted to result in the sensation that the pitch has decreased by a factor of one-
half. The results are shown in Table 6, where the first row is the frequency of the standard
tone. The second row is the mean frequency of tones which were selected by twelve
-25
100
ZOOG
200 5OO
Ereque'ncy In Cycles per Second
FIG. 20. Pitch Change of Single-frequency Tones at High Levels. (Snow.)
2000
observers to be one-half the pitch of the standard. The loudness level of all tones was
40 db. Table 6 shows that a tone of 373 cycles will appear to be one-half as high in pitch
as 1000 cycles. By use of these and other data on estimations of pitch intervals, Stevens,
Volkmann, and Newman have devised a numerical pitch scale having the property that
tones which appear to be 50 per cent lower in pitch will also be related in the same manner
on the pitch scale. The unit of pitch is called a *'melT" and the relationship between mels
and frequency for pure tones at a loudness level of 40 db is shown in Fig. 21.
BOOO
20
100 200 400 1000 2000 4OOO 10,OOO
Erequency
FIG. 21. Relation of the Pitch in Mels to the Frequency of Tones at a Loudness Level of 40 Db.
(Stevens and Volkmann.)
12-18 ACOUSTICS
7. LOCALIZATION OP SOUNDS
The ability to localize the direction and to form a judgment of the distance away of a
source is a matter of common experience, but very few quantitative data on the subject
are available. The localization of direction (angular localization) appears to depend upon
the detection of phase differences at the two ears, loudness differences, differences in
quality, and differences in arrival times at the two ears. Loudness differences, and quality
differences (in complex sounds) , and to some extent phase differences, arise from diffrac-
tion effects of the head. At low frequencies the loudness difference at the two ears is
small r but localization by phase difference is effective. An angular accuracy of about
±10° is obtained for sounds directly in front or in back of the observer. Much less preci-
sion is obtained when the source is at one side. Loudness differences are most effective
in the frequency range above 3000 cycles and quality differences in the range above 1000
cycles. In general, complex sounds having prominent high-frequency components, hence
large loudness and quality differences between the ears, are localized with greatest accu-
racy. Under familiar acoustic conditions, such sounds may be localized frequently by
the use of one ear only. Presumably this is accomplished by recognizing the characteristic
distortion introduced by the head. Steinberg and Snow report that the apparent distance
of the sound source, i.e., depth localization, depends upon the loudness of a sound. When
an observer is listening in a room, the ratio of the direct sound intensity (that reaching
the ears without reflection) to the reflected sound intensity also enters into depth localiza-
tion.
BIBLIOGRAPHY
American Standards Association, American Standard Acoustical Terminology, J. Acous. Soc. Am.f
Vol. 14, 84 (July 1942).
Beasley, W. C., Characteristics and Distribution of Impaired Hearing in the Population of the U. S.,
J. Acous. Soc. Am., Vol. 12, 114 (July 1940).
Bekesy, G., Clicks and the Theory of Hearing, Physik. Z&itschrift, August 1934, p. 577.
Dimmick and Olson, Intensive Difference Limen in Audition, J. Acous. Soc. Am., Vol. 12, 517 (April
1941).
Fletcher, H., Loudness, Masking and Their Relation to the Hearing Process and the Problem of Noise
Measurement, /. Acous. Soc. Am., Vol. 9, 275 (April 1938).
Fletcher, H., Loudness, Pitch, and Timbre of Musical Tones, J. Acous. Soc. Am., Vol. 6, 59 (October
1934).
Fletcher, H.T A Space-time Pattern Theory of Hearing, J. Acous. Soc. Am., April 1930, p. 311.
Fletcher, H., Auditory Patterns, Rev. Modern Phys., Vol. 12, 47 (January 1940).
Fletcher, H., Speech and Hearing. Van Nostrand (1929).
Fletcher, H., The Mechanism of Hearing, Proc. Nail. Acad. Sci., Vol. 24, 265 (July 1938).
Fletcher and Munson, Loudness, Its Definition, Measurement, and Calculation, J. Acous. Soc. Am.*
Vol. 5, 82 (October 1933).
Fletcher and Munson, Relation between Loudness and Masking, J. Acous. Soc. Am., Vol. 9, 1 (July
1937).
Galambos and Davis, The Response of Single Auditory-nerve Fibers to Acoustic Stimulation, J. Neuro-
-physiol, Vol. 6T 39 (1943),
Inglis, Gray, and Jenkins, A Voice and Ear for Telephone Measurements, Bell Sys. Tech. J., April
1932, p. 293.
Knudsen, V. O., Sensibility of the Ear to Small Differences of Intensity and Frequency, Phys. Rev.,
January 1923, p. 84.
Rawdon-Smith and Sturdy, The Effect of Adaptation on the Differential Threshold for Sound In-
tensity, Brit. J. Psych., Vol. 30, 124 (1939).
Riesz, R. R., Differential Intensity Sensitivity'of the Ear for Pure Tones, Phys. Rev., May 1928, p. 867.
Shower and Biddulph, Differential Pitch Sensitivity of the Ear, J. Acous. Soc. Am., October 1931,
p. 275.
Sivian and White, On Minimum Audible Sound Fields, J. Acous. Soc. Am., April 1933, p. 288.
Snow, W. B., Change of Pitch with Loudness at Low Frequencies, J". Acous. Soc. Am., Vol. 8, 14 (July
1936).
Steinberg, J. C., Positions of Stimulation in the Cochlea by Pure Tones, /, Acous. Soc. Am., VoL 8.
176 (January 1937).
Steinberg, Montgomery, and Gardner, Results of the World's Fair Hearing Tests, J. Acous. Soc Am
Vol. 12, 291 (October 1940).
Steinberg and Snow, Auditory Perspective — Physical Factors, Elec. Eng., Vol. 53, 12 (January 1934).
Stevens, S. S., The Attributes of Tones, Proc. Natt. Acad. Sci., July 1934, p. 457.
Stevens, S. S.t and H. Davis, Hearing, Its Psychology and Physiology. John Wiley (1938).
Stevens and Davis, Psychophysiological Acoustics — Pitch and Loudness, J. Acous. Soc. Am , Vol 8
1 (July 1936).
Stevens and Volkmann, The Relation of Pitch to Frequency: A Revised Scale, Am. J. Psych Vol 53
329 (July 1940). ' '
Stevens, Volkmann, and Newman, Scale for the Measurement of Pitch, J". Acous. Soc. Am., Vol. 8, 185
(January 1937).
Stewart, G. W., Localisation of Pure Tones, Phys. Rev., May, 1920, p. 425.
Trimmer and Firestone, An Investigation of Subjective Tones, J. Acous. Soc. Am., Vol 9 24 (July
1937),
Troger, J., The Reception of Sound by the Outer Ear, Physik. Zeitschrift, January 1930, p 26.
Waliaeh, Fam, On Sound Localization, /. Acous. Soc. Am.t Vol. 10, 270 (April 1939).
PRODUCTION OF SPEECH 12-19
Wegel and Lane, Auditory Masking and Dynamics of the Inner Ear, Phys. Rev., February 1924, p. 266.
Wever E.G., The Electrical Responses of the Ear, Psych. Bull., March 1939, p. 36.
Wnghton, Sir Thomas, Analytical Mechanism of the Internal Ear. Macmillan, London (1918)
Zurnmhl, G., Variation of Pitch Sensation with Loudness, Zeit f&r Sinnesphysiologie, August 1940,
SPEECH AND MUSIC
By John C. Steinberg and W. A. Hanson
8. DESCRIPTION OF SPEECH ORGANS
The speech organs consist of the lungs and respiratory muscles, the trachea or wind-
pipe, the larynx, and the cavities of the throat, mouth, and nose. In speaking, a Sow of
air is produced by the lungs which is modified in passing through these passages to form
speech sounds. The larynx is a cavity of irregular shape formed of cartilage located at
the upper end of the trachea, a tube some 12 cm long and 2 cm in diameter leading from
the lungs. A pair of muscular ledges, called the vocal cords, form a slit in the larynx
through which the air must pass. When the vocal cords are set in vibration, the air flow
is periodically interrupted and the sound is said to be voiced. Measurements reported
by Riesz, on persons whose larynx had been removed by a surgical operation, indicate
that the excess pressure in the lungs when producing sustained parts of speech, such as
vowels, is of the order of 4 mm of mercury or 0.005 atmosphere. The rate of air flow is
about 150 cu cm per sec. The normal capacity of the lungs is about 2500 cu cmT and the
average expiration in breathing is about 500 cu cm.
By means of high-speed motion-picture photography, views of the vocal-cord movements
in slow motion have been obtained at Bell Telephone Laboratories. Measurements on
successive exposures of the vibrating cords indicated a displacement amplitude that was
sawtooth in form. The cords tended to snap apart and close slowly and firmly together.
The wave form contained a fundamental and higher harmonics which diminished in
amplitude inversely as the square of the harmonic number. The length of the cords and
maximum amplitude of opening varied with pitch. For example, in the subjects studied,
the cords were about 1.2 cm in length and their widest opening was about 0.4 cm when
vibrating at 120 cycles. At 300 cycles, their length was about 2.0 cm and the widest
opening about 0.2 cm. Changes in the acoustic load by closing the mouth opening with a
glass window or filling the vocal cavities with helium did not appear to affect the vibration
wave form of the vocal cords markedly.
The opening between the cords is called the glottis, which, of course, varies in size as
the cords vibrate. There appears to be little direct information on the acoustic wave form
produced at the glottis by the vocal-cord vibrations. Indirect evidence based on harmonic
analysis of vowel sounds reported by Steinberg and also Lewis indicates a sawtooth wave
form in which the amplitudes of the harmonics dinunish inversely as the 1,5 power of the
harmonic number.
9. PRODUCTION OF SPEECH
MECHANISM OF SPEECH. As has been discussed by Dudley, speech may be re-
garded as a phenomenon of modulation in which the breath stream, a unidirectional Sow
of air produced by the lungs, is given intelligence-carrying variations. The breath stream
is made audible by two kinds of modulation called weal-cord and frictional modulation.
The first is produced by the periodic interruption of the breath stream by the vibrations
of the vocal cords. The second is produced by the turbulent flow of the breath stream
through constrictions formed in the vocal tract. Both produce variations at relatively
high rates, i.e., in excess of 70 cycles. The vocal-cord modulation produces fundamental
and harmonic overtones such as characterize a vocalised: or voiced sound. Frictional
modulation produces a wide range of inharmonically related overtones such as character-
ize a hiss.
The audible components thus produced are in turn modulated by relatively slow varia-
tions, i.e., at rates definable by frequency components in the range below some 40 or 50
cycles. One of these is called start-stop modulation, which is accomplished by the muscles
of respiration, the vocal cords, tongue, and lips. Another, called cavity modulation, is
produced by changes in size and shape of the vocal passages extending from the glottis to
the mouth and nose openings. These passages selectively transmit and radiate the audible
frequency components produced in the breath stream by vocal-cord and frictional rnodula-
12-20
ACOUSTICS
tion. This results in a reinforcement, relatively, of certain frequency components or
regions which are called vocal resonances.
Several other types of low-frequency modulation occur such as inflection, vibrato, and
stress, but the four noted above are the ones of chief importance to the intelligibility of
American speech sounds. Start-stop modulation is one of the principal characteristics of
the plosive or stop consonant group, and frictional modulation is one of the chief charac-
teristics of the fricative consonant group. In the vowel and vowel-like group of sounds,
cavity and vocal-cord modulation are among the conspicuous characteristics.
CHARACTERISTICS OF SPEECH SOUNDS. As a result of cavity modulation, all
sounds tend to show characteristic frequency regions of reinforcement in a greater or less
degree. These vocal resonances are more conspicuous in the vowel and vowel-like sounds.
In general, there is a resonance in the range from 300 to 1000 cycles, one hi the range from
1000 to 2500 cycles, and one or more in the range from 2500 to 4000 cycles. The two
resonances below 2500 cycles are the ones that vary most in frequency position from
sound to sound. There has been a tendency to associate the low resonance with the
pharynx or throat cavity and the next resonance (1000-2500 cycles) with the mouth
cavity. Damping constants reported for the cavities range from 1000 to 4000 db per sec.
With a vocal-cord vibration rate of 125 cycles, the cavities would be excited periodically
at intervals of 0.008 sec, and the amplitude of the sound wave would be expected to decay
to something between 0.4 and 0.03 of its initial value during the interval.
Table 1. Approximate Characteristics of Common Speech Sounds
Sound
fi
Li
h
L2
h
Ls
/4
U
n
Pure Vowels
e (eve)
350
ij
2400
-17
3200
-13
3700
-73
6.
44
i (it)
450
_4
2150
7950
3600
10.
27
e (bet)
550
-3
1950
-9
2700
-13
3700
-19
6.
60
a" (at)
800
— 1
1800
2800
3900
6.
89
ah (father) . .
800
0
1250
-8
2950
-22
3800
-30
6.
52
a fall)
550
0
850
2900
4
15
o (obey)
450
-2
800
-9
2600
-24
3200
—24
4
74
u (foot)
400
-2
1050
-12
2300
-24
3200
—34
2
96
u (boot)
350
—4
950
—19
2250
-32
3200
-34
6.
26
Vowel-lite Sounds
1 (let)
450
—8
1000
—21
2550
-20
2950
—24
tti
4 31
n/
8 40
r (run)
500
-5
1350
—12
1850
-16
3500
—29
2 78
13 05
m (me)
FundRTnppt^
-11
1250
-21
2250
-23
2750
-30
5.89
5 48
u (no)
u
— 13
1450
-26
2300
-28
2750
—33
4 99
12 52
ng (sing) . ...
u
-to
2350
2750
3 57
Fricative Consonants
v (voice)
Fundamental
— 18
1150
-37
2500
3650
12 (3 9}
42 n 4}
th (that)
— 18
1450
-27
2550
—45
67 (20)
I 2 (0 04)
z (zoo)
u
— 16
2000
—33
2700
—42
03 (5 4^
6/1 c\ \\
zh (pleasure)
«
-15
2150
—24
2650
-39
0 02 (1 7)
0 01 (0 3)
Stop Consonants
b (be)
Timctamftntal
—20
800
1350
46 (25)
04 (\ 7\
d (day)
-20
1700
2450
62 (78)
4 4 M4^
g(get)
fa
17
Variable
>
4.3 (5.5)
0.4 (2.8)
The steady-state resonance characteristics of the sounds can be expressed by the peak
frequencies /t- of the vocal resonances, the levels Li of the peak frequencies, and the damp-
ing constants A* expressed in decibels per second which indicate the sharpness of the
resonances. This information, together with the data on the acoustic wave form at the
glottis given in article 8, permits an approximate construction of the spectrums of the sounds.
The available data on these characteristics are summarized in Table 1. The columns
designated /i to /4 indicate the peak frequencies of vocal resonance. They were obtained
from data reported by Kopp and Green, and represent values for one voice. Since the
values vary somewhat from voice to voice, values for a single voice were chosen to permit
a relative comparison of the different sounds. When "fundamental" appears in the col-
umn fi, it means that the resonance was too close to the fundamental frequency to be
resolved by the analyzing means. The vocal resonances shown for the voiced consonants,
77, th (that), z, zh, 6, d, and g, apply also to their unvoiced cognates, /, th (thin), s, sh, p,
t, and k. For g (get) and also k (key) , the frequencies of the vocal resonances vary depend-
ing upon the sound with which they are combined. The column LI shows the relative
levels of the first resonance peaks as derived from Table X, Fletcher, Speech and
Hearing.
PKODUCTION OF SPEECH 12-21
The remaining columns, L2 to L4f show levels of the respective resonant peaks based on
data from several sources. All levels are expressed in decibels below the level of the first
resonant peak in ah (father). The damping constants A,- are not shown but vary from
about 1200 db per sec for the first resonance to about 4000 db per sec for the fourth res-
onance. The band width of the resonance at points on the resonance curve 3 db below
the peak response is given approximately by A,-/27.3. The last column, designated n,
shows the relative occurrence of the sounds in telephone conversation from a report by
French, Carter, and Koenig. The figures indicate the percentage occurrence of the vowels
shown among all vowels occurring in 95,522 vowels. The occurrence figures are indicated
separately for initial and final consonants from 64,043 initial and 65,544 final consonants.
The figures in parentheses indicate the occurrence of the unvoiced cognates of the voiced
consonants shown. The figures were obtained from the words, syllables, and sounds
occurring in telephone conversations after the exclusion of articles, names, titles, exclama-
tions, letters, and numbers.
An interesting feature of the report is the extent to which a few common words or
sounds, by being used over and over, from a large part of ordinary speech. For example,
eight different words and four different sounds account, respectively, for 25 per cent of
the total words and sounds used. Thirty words and ten sounds account, respectively, for
50 per cent of the total used.
ARTIFICIAL LARYNX. The artificial larynx is based on the principle that the vocal-
cord tone need not necessarily arise in the larynx in order that cavity modulation occur to
form speech. It may be introduced into the vocal cavities through the mouth opening.
A means for accomplishing this has been described by Riesz and is used by persons who
have had their larynx removed by surgery. In this case, the windpipe is terminated by
a small opening in the neck, through which the patient breathes. In using the artificial
larynx, a flexible rubber tube is fitted over the neck opening and leads to a reed which
vibrates with the passage of air. The vibrated air stream is led to the mouth opening by
a flexible tube, and, with practice, the patient learns to modulate the sound and form
speech by the ordinary articulatory movements. Firestone has described and demon-
strated a form of artificial larynx for introducing various types of sounds through the
mouth opening for vocal modulation. Mr. G. M. Wright has developed an artificial
larynx in which sound is introduced into the vocal tract by means of vibrators attached
outside the throat. The device has been used to produce unusual vocalised sound effects
in radio work.
ARTIFICIAL VOICE. An artificial voice described by Inglis, Gray, and Jenkins,
designed for the measurement of microphones, consists of a small moving-coil loudspeaker
having an opening somewhat larger than that of the human mouth. Its design provides
for an undistorted acoustic power output comparable with powers produced in speaking.
Its sound field approximates that of the human mouth to the extent that the loss in power
delivered by a microphone with increasing distance between the mouth and the micro-
phone is about the same for the artificial as for the human voice.
TEE VOCODER. A means is described by Dudley for continuously analyzing speech
and utilizing the results of the analysis to synthesize or remake the speech. It is based on
the principle that the intelligibility of speech is carried by the relatively low-frequency
components produced by cavity modulation and that the "buzz tone" (vocal-cord modula-
tion) and the ''hiss tone" (frictions! modulation) simply act as carrier waves which are
modulated by the vocal cavities. Frequency range reduction is achieved by transmitting
only the low-frequency modulations and employing them to modulate locally generated
buzz and hiss tones. In one variation called the voder, speech is produced artificially
by using a keyboard manipulated with the fingers for generating the carrier waves and the
low-frequency modulations.
VISIBLE SPEECH. A development described by Potter, in which speech is continu-
ously analyzed and the results of the analysis portrayed to the eye in the form of visible
patterns that one can learn to read, holds possibilities in the fields of visual hearing and
visual telephony for the deaf, phonetic printing and retranslation into sound, the selective
operation of automatic devices by voice sounds, and in the specialized fields of phonetics,
linguistics, foreign language, music, etc To obtain readable patterns of speech sounds,
the portrayal emphasizes the modulations that are important to intelligibility as illus-
trated in Fig. 1. Frequency is shown vertically, time horizontally, and intensity by shades
of gray. The stop gap (start-stop modulation) , the plosive release (frictional modulation) ,
and the voice bar (vocal-cord) modulation are indicated for the voiced stop consonant b.
Likewise the vocal resonance bars (cavity modulation) are indicated for the vowel e. The
u shows only two resonance bars which differ in position from those of the e. The transi-
tion from e to u is shown also. The fricative fill for / is an example of frictional modula-
tion. The patterns for voiced sounds show regular vertical striations, the space between
12-22
ACOUSTICS
the striations indicating the pitch. Note the drop in pitch toward the end of ^fiye."
The unvoiced sounds (frictional modulation) show irregularly spaced vertical striations
indicating a lack of pitch. The patterns are read from the characteristic modulations of
the sounds and the transitions between them.
Voice bar for "8"
_Stop gap for "W
Plosive release for "B"
IflosTve release for "T"
Fricative fill for
~r
0.6 0.8
Time in seconds
B E U P A T F 1
FIG. 1. Visible Patterns of the Words "Be up at Five"
10. SPEECH POWER
Since the wave forms of speech are complex, different types of speech power have been
defined as follows:
Instantaneous. The rate at which sound energy is being radiated by the speaker at
any given instant.
Average. The average speech power for any given time interval is the average value
of the instantaneous speech power over that interval.
Peak. The maximum value of the instantaneous speech powers occurring in a given
time interval.
Phonetic. The phonetic speech power is the maximum value of the average speech
power in 0.01-sec intervals of a vowel or consonant sound. It is the maximum value of
the envelope that results from plotting average power for 0.01-sec intervals against time,
as the sound grows, remains steady, and decays.
The quantity usually measured is the speech pressure at some convenient distance and
direction from the mouth. Dunn and White have reported the results of measurements
of various types of speech pressure and comparisons with earlier measurements, and Dunn
and Farnsworth have reported on the directional characteristics of the mouth as a radiator.
The results are summarized in Table 2. They comprise statistical measurements of speech
pressure vs. frequency range for conversational speech made with an arrangement for
introducing any one of 14 band-pass niters into a speech circuit. The frequency range
below 500 cycles was covered in one-octave steps. Above 500 cycles, each filter passed a
range of about 1/2 octave. Provisions were made for measuring instantaneous, peak, and
rms pressures in alternate time intervals of Vs sec and also, for certain cases, in time
intervals of 15 sec. Some 600 intervals of Vs sec were usually measured for a given con-
dition representing an integrated time of 75 sec.
From the results it is possible to calculate the various types of speech power. This is
done by converting pressure to power per square centimeter (intensity) by the relation
jf = p2/415, where I = intensity in microwatts per sq cm and p = pressure in dynes per
sq cm at a given distance and direction from the mouth. The intensities in other direc-
tions are obtained by weighting in accordance with the directional characteristics of the
mouth, and P, the total power radiated, is then obtained by integrating over a spherical
surface having a radius equal to the distance. The results of such calculations are given
in the first row of Table 2 in the form of ratios expressed in decibels. The ratios depend
upon the distance and direction from the mouth and the frequency range in which p is
measured. The reference position is designated as 30, 0°, 0°, signifying 30 cm from the
mouth at zero azimuth and altitude angles, i.e., directly in front of the mouth. The values
when added to p expressed in decibels from 1 dyne per sq cm give P expressed in decibels
from 1 microwatt. The values are based on distribution measurements for one voice.
SPEECH POWER
12-23
^
«\
,—
c^
WV
t<\
0
0
o ^
G3
o*
vO
C4
-^r
^
—!
j^
*o
o
tn
CO
^
r-j
•0
o
OO
rs
r>*
1
00
t
oo
"•*§
t
I
I
I
1
i
1 i
t
, 2
fN
^
^
C^
vO
0
o
1
0
go
OO
00
m
O
^i
CvJ
00
oo
o
s
ON
iX
3
in
o
0 -0
^5
CN
c^t
t
i
t
r*
<s
1
—
^ 1
^vrv
1
I
!
I
1 !
i ?
c*v
OX
r^
vO
i
rs
0
0
^
0
og
o
0
0
vO '
O
oo
o ««•
01
f
fS
1
I
1
I
f
•o
i
"° i
!
, £
^
—
«^»
«^
00
0 :
o
^
1
*ft
0°
0
00
fS
^1
0
CN
•*»•
*r\
0
o
c<"\
O1^
o
ro
«o
^
cvi
og
CS
1
1
ir»
tr»
i
I
1
i
I
I
\ i
1
, ^
0
00
^*
CO
^r
0
o
0
So
c»
cr»
>o
^
—I
0
rvj
en
CO
o !
_I
<o
cs
O^
o.
10
—
»—
*""
"™"
t
1
""
«M
~~
-«• !
I
I
"*
i ;
^ !
"~CS
I
i
I
±1
oo
-
-
<N
—
^
0
*n
i|
0
OJ
T
vO
T
7
1
pm
in
0
o
7
s
I
—
3
0
1
^
t^
-0
^
o
OO
o
x^
1
io
«<^
<^t
<rv
~
o
0
^
r^
«ft
0
<H
0
0
c^
^r
<=>
-^
O
I
1
1
0<
—
f
r
•S
«n
<*\
ea
«A
O
o
0
«
o*
&
go
21
i
2
[
o
J
±
2!
2
-«•
"*
0
r*
s
0
•«-
03
ci
10 ^*
I
o
ON
^_
ON
_
tA
*Tk
0
xo
1
*^0
^
C-4
u-v
^
_r
0
IA
P^
t*\
Irt
l^
*n
SO
oo
«n
in
Q
^s
1
1
I
I
VM
0
?
m
1^
0
^5
^
«-i
0
0
>>
"^^
f\
p^
CO
^
^J
0
^jl
^
0
.
o>
<st
_
0
o
—
0
S
^~«Q
—
1
I
I
I
—
""
0»
C-*
S
s
s •
» :
^e :
5i
I y
r-.
xO
>o
• —
•O
a -
E *
s '
Ol
to v
*
•^•
*
o
o
G>
vO
__
*
*— 1 "
J2 •
csi^s
—
1
i
I
—
? es
' >"§
HJ
1
e4
0>
I
c -3
"S >
^
s
si _:
s
1
H
Whole
pectrum
d
0
oo
o
i
0
oo
C3
1
0
i
T
0
0
of intervals
from long-i;
whole spec
Is
^00
So
o
*0
from long-
iterval rms
whole
peotruin
of speakers
CQ
o
P ft
£»•-
_a.s **i ED
^o
,£3—*
!
&-
T3
T5
^
~5
e^
T5
S3
n
Sd1|
f . S a
5 S £
Quantity
in dynes/cm2 at 30, 0°, 0°. 1
d
S
Women. .......
1
3-
0
1
0
cT
*A
il
0
0
o~
H
o
0
o"
O
oo
O*
-
0
of rms p in l/s-sec intervals
db from long-interval rma
vale in which 1/8-sce rme p ext
fai rms p by the indicated amoi
of inatalltaneous and 1/8
, of time that instantaneou^
seeds long-interval rms p by i
unta.
of long-interval rms p am
% of speakers for which 1<
tiB p exceeds average long-inte
ndicated amounts
s in 1/8-BGG intervals ex-
db from long-interval
, 0°, 0°, Peaks exceeded
)% of intervale
•s-
g^ro
p, OQ
*^ ~
"^ g {1,
** C3^ -—
e c ** £
^ QX S °
S3
2 . " S
X> oi
o3 M
o£S
K^ "oil
".3 'C S'jS
12 £J*sJ*3
!a|
-1^1
is-Se
^1&-
IsN'i
llil
fc| S
^•g
^o1^
d-_2^^
*3 P,§.S
Tg ft^,3
"« EEo
"? ^ c
Sr
3
a
fS
h
5
2
12-24 ACOUSTICS
The second and third rows give the long interval rms pressure pat 30, 0°, 0° in decibels
from 1 dyne per sq cm. The rows designated "men" and "women are averages lor b male
and 5 female speakers, respectively. By long interval is meant a time average over some
600 i/s-sec intervals or 75 sec. Corresponding values in other bands may be obtained by
taking p2 as proportional to band width in cycles per second. Rows 4, 5, 6, and 7 show
pressures p at different directions relative to the reference position. The mouth radiates
maximally in a direction about 45° down from the horizontal. Rows 8 and 9 show peak
pressures that are exceeded in 1 and 10 per cent of the i/g-sec intervals relative to the
long-interval values. One per cent peaks more than 20 db above long-interval pressures
occur frequently. Corresponding values for other bands may be obtained approximately
for peaks occurring less than 10 per cent of the time, by proceeding as though they were
rms pressures. The peak-factor data are essentially the same for both men's and women's
speech.
Rows 10, 11, and 12 show the distribution of i/s-sec rms pressures relative to the long-
interval values given in rows 2 and 3. Distributions for the three low-frequency bands
are very similar to the whole spectrum distribution, row 11. Distributions for the remain-
ing bands are very similar to that for the 700 to 1000 cycle band given in row 12. These
distributions are about the same for both men's and women's speech.
Rows 13, 14, and 15 give distributions of instantaneous and peak pressures relative to
the long-interval rms pressure. The distribution for instantaneous pressures is based on
data for a single male voice.
The last two rows give data on the distribution of long-interval rms pressures among
various speakers reported by Fletcher.
The results in Table 2 indicate a long-interval total speech power, averaged for 6 men,
of 34 microwatts. The corresponding figure averaged for 5 women is 18 microwatts.
These values are somewhat larger than that of 10 microwatts given formerly. Some 2 db
of this difference is due to the method of converting measured pressures to radiated powers.
These values obtain for continuous connected speech. If the silent intervals (about 1/5
to 1/3 of the total time) are excluded, the average is increased about 25 to 50 per cent.
The above values hold for about 30 per cent of the speakers. One per cent of the speakers
may radiate powers in excess of 272 microwatts. If one shouts as loudly as possible,
the total power may reach 3400 microwatts, an increase of 20 db. For a very faint but
intelligible whisper, the total power may fall to 0.0034 microwatt, a drop of 40 db.
In 1 per cent of i/s-sec intervals, the peak power may exceed the long-interval total
power in connected speech by 20 db. Thus total peak powers of the order of 3400 micro-
watts may be reached by average male voices.
The ah (father) is about the loudest sound in speech. Fletcher reports a total phonetic
power of 41 microwatts for this sound. Corresponding values for other sounds may be
obtained from the column designated Ll of Table 1. These obtain for discrete words or
syllables spoken at conversational level. Peak powers of the order of 1600 microwatts
for the ah sound were obtained under these conditions. Wolf, Stanley, and Sette report
total phonetic powers of 1 watt when the vowel ah is sung by professional singers. To be
consistent with the data reported in Table 2, the total phonetic powers given above should
be increased by 2 db.
Sivian reports on changes in the frequency distribution of speech power as a speaker
changes from a low (confidential) talking level to a normal (conversational) level and to a
high (declamatory) level. The total change in power from low to high was about 24 db.
In general, power .was transferred from the frequency range below 500 cycles to the range
between 500 and 4000 cycles as the talking level was raised. To be representative of
declamatory speech, the values in the bands below 500 cycles given in row 2, Table 2,
should be decreased about 4 db and values between 500 and 4000 cycles should be in-
creased about 3 db.
11. POWERS PRODUCED BY MUSICAL INSTRUMENTS
In music, as in speech, various aspects of power — peak, average, etc. — must be dealt
with. A comprehensive report on the powers produced by the various musical instru-
ments and by orchestras has been given by Sivian, Dunn, and White. The report also
describes in some detail the band-pass filter apparatus discussed in article 10 on speech
power. Two types of measurements were made on the waves, the average pressure
in 15-sec intervals and the peak pressures in i/s-sec intervals. The pressures are the field
pressures at the position in the field where the microphone of the measuring circuit was
placed. For the measurements on individual instruments, the position of the microphone
with respect to the source varied with instrument. For the orchestra, the microphone
POWERS PRODUCED BY MUSICAL INSTRUMENTS 12-25
CO
"3
'
«*H
'*•'.
CJ
°
0 0
0
O
0
=> 0 «A
o
0
0
0 fcr
\ 0
? 0
=> o
fL| S °
3
~
—
— '
—
0
•A cs
-1-
00
-
•^r
- -*•
— oc cs
«r
rs
vn
t-.
• es
—
— CS
O
a
i— i
111
1
00
^
t>.
c£
0
00 00
3 0
00
s
eo
O
5
O
0
0 0
m — c
000
c
0
o
CN
o
NO «r
"i cs
0^
H^£
£
ON
"
en
0
o
0 0
0
O
O
0
0 0
O 0 0
0
0
e
0 C
S 0
5 m
0 0»
0
M
0
o
o
o
«n
•* <«•
en
O
co
in
en m
0 ui cs
PS
t
^
-*
^«- <
- 0
0 0.
||
£
CS
«•»
cs
CA
0
CO
cs
=
NO NO
~
IN.
•s
S
S S
t>J m" oo
cs —
t>
^
tr
k
s s
« es
4 rs
n •«•
0 0
oo •*•
Tj&
§?
0
0
co
m
0
— 00
m
»A
ON
0
T «n
oo r»
. NC
>
cs
•«
— a
9 en
o cs
0
S
1
en
CS
eo
CS
0
en 0
en
en
CS
0
cs —
«<% <=
t <=,
>
0
C
}
cs r
•« —
— o
~
C £
T5"3 2
o
o
O
o
o
o
lA O
O
0
o
g
00
t i
c
> c
> c
?
>
>
0
o
o
C
C
ex
>
S
9
0 C
O C
D 0
S CO
o
=> -
^
al£
PQ g <s
£
cA
rs
lA
cs
cs
i
^
NO
csiA
•O CS
1
0
es
I
0
o
i
cs «n
in \r
0 c^
m ti-
cs CN
! i
J P-
3
cs
0
c«
C
c
4
>
>
0 C
tn t
cs c
*> rs
n es
s o
n ~~
Q o
o
«n
rs
o
t
06"
00
•1
0
o
m
•A
0
o
O
o
c
S
0
C3 U1
\ 0
m
0
t»n
0
O
0 0
0
0
o
fe
NO
_
cs
p.^
L._
cs
in
1^
«J
-i
oo
NO W
^ _
__
cO
o
0
NO
— •o
^ _
vO
CD
•4^
cs
—
en
— i
C
M
NO
on
ND
^.
^.
m
'"f
__
j^
3*g |
£
vO
-«-
ON
trv
in
O
tn
00
<4
f
CA
s s
\ m
> O
O
§
oo
O
0
NO
CS
D CS
tn
NO
£-(P^p?
^.
en
_
ON
0
0
o
O
N|
D
0
0 C
3 O
o
o
0
0
0
>• cs
NO
cs
CS
^
*"*
O
0
O
O
CO
eo
^
cs
c
3
cs
o ^
' NO
00
«<*•
oo
*«•
-»
» cs
0
0
H
m
o
,_,
>A
o
m
^
on
en
0
O
^r
rsC \c
> UI
CS
NO
n
vn
en
O en
O
o
3**
V
NO
OO
NO
NO
cs
r
S
1 CS
cs
•s o
||
PH
CS
en
f
S
PH o
1
o
0
NO
0
en
es
_ .
^
it
1
NO
00 C*
NO
C
4
NO
ON
NO
0
.S*^
o
ON
m
^T
00
cs
^T
^-
in
V
D
CO
en e*
__
c-
4
cs
r^.
««•
0
*
en
OS
-do
0
0
6
fe
cb°
2-S
S
"H
*5
£
'is
•8
a
tri
11
§«
CD ^
.a
T)
**o
**&
4
J3
I
1
o
measu
ttaohed
0
o
^t
ileverbe
of 3 me
0
o
-3
o
5
g-c
1
§§
11
>,
1
o
.28
eS
£2
=J
1
£
-" £
II
1
S3
Microphone Position and Assu
rinnvoTf.inor t,n Total Sound
1
i
i
3 ft in front, on axis. Radiation
cylinder having drum diameter.
4 ft in front, 90° off axis. Peak pree
8.5 db for l-ft distance. Radiati
hemisphere.
3-ft distance. Peak pressure incre
1 ft. Radiation confined to hem
3-ft distance. Conversion as for c
3-ft distance. Radiation confined
3-ft distance. Radiation confined
3-ft distance. Conversion made
ments with a complex sound BOUI
a horn of similar sire.
(
>tt custance. Conversion as lor t
3-ft distance. Conversion as for t
s
k3
1
3
2
§
n
<
c
1
1
J
c
•<
i
2,
u
S
i
\ O-f t distance. Room 29' X 29' X 1 3
tion time 1 sec, 60 to 4000"", ave
odfl (see text).
16 ft from nearest instruments, in
piano. Average of 2 methods (s
1 5 ft from nearest instrument in th
Effective distance 1 5 ft. Radiatio
form over 1/4 sphere.
i
X
X
o
1
1
M
X
3
jd
IrO
i
1
Bass drum 3(
Base drum 3(
Bnare drum
I
a>
•Q
1
Baas viol
Bass saxoph
.0
5
1
1
£
Trumpet
French horn
Clarinet
*
i
i
i
I
o
"o
0
S
S
1 5-pieoe ore
75-pieoe ore
Pipe organ
12-26
ACOUSTICS
was placed near the conductor's stand. By making assumptions as to the radiating prop-
erties of the instruments, and of the orchestra, their total power outputs could be estimated.
Table 3 gives the average and peak pressures at the positions of measurement as indi-
cated. The columns "total peak power" give the total power radiated by the instru-
ments computed on the basis of assumptions indicated in the table. The left half of the
table applies to the whole spectrum; the right half to the bands containing the maximum
*** An 'average of three methods was used for determining the total power radiated by the
piano. In the first method, the diffuse pressure in a room of known reverberation was
measured and the power calculated. In the second method, from auxiliary measurements,
it was shown that the measured diffuse pressure was the same as if the total power output
were distributed over a sphere of radius 5.37 ft. In the third method, the diffuse pressure
was compared with the pressure measured in the opening between the raised top (grand
piano) and the sounding board. The radiated power was assumed to be uniform over
the area of the opening, 3 ft by 6 ft. The three methods gave peak powers of 0.166, 0.437,
and 0.198 watt, respectively.
The measurements on the 15-piece orchestra were made in the same room as the piano
measurements, and methods 1 and 2 were used to obtain the total power. The sounds
from the 75-piece orchestra were picked up in a theater, and suitable acoustic data for
using the above methods were not available. It was assumed that the radiation was
uniform over a hemisphere of 15-ft radius. The measurements on the pipe organ were
made in the same theater.
Because of the uncertain assumptions in calculating total powers, the measured values
of pressure are also given in Table 3. The peak pressures were measured within a range
of db3 db, and the percentage of i/s-sec intervals that the power fell within this range is
indicated. The peak pressures are useful in determining the amplitudes that pick-up
instruments and amplifiers must handle, and the total peak powers for determining the
requirements that must be met by power amplifiers and loudspeakers when reproduction
of the original level is desired. The most powerful single instrument is a bass drum, which
radiates a power of about 25 watts, primarily in the low-frequency ranges. A large orches-
tra is capable of radiating power of about 60 to 70 watts. This is about 70,000 times the
peak power of speech.
Figure 2 (from Fletcher) shows the frequency distribution of the maximum and most
probable peak powers for a 75-piece orchestra. The curves are based on average measure-
ments of four selections which gave whole-spectrum peak powers from 8 to 66 watts, and
! Average Power fri db
M M tO
n o 01 o 01 a
^-
• "~
*"*^
4.
/
/
^"••»«i
-— .
— '
^ ^
X
/
/
/
/-—
\
^
"-x.
/
/
/
f
X
£ ,n
/
/
— ,
v,
Powe'r DOT Octave to
. A A A .
D Ol O Ol C
/
^N
/
\
V
/
\
1 • M*c*krrum Peak Powers in -^Second Intervals
2 - Most Probable Peak Powers in % Second Intervals
Total Average Power =0.1 Watt CApproxO
\
*S
° OR
eg
-4q
2.7 65.4 130.8 261.2 523.2 1046 2092 4185 8370
Frequency in Cycles per Second
234 567 89101.
Frequency Level in Octaves from 16.35 Cycles
FIG. 2. Maxim mm and Most Probable Peak Powers
average powers from 0.08 to 0.13 watt. The zero line corresponds to an average power
of about 1/io "watt. The ordinate is the ratio expressed in decibels of the peak power per
octave to the whole-spectrum average power.
A violin player, when asked to play at the lowest level that could be used with an
TESTS OF SPEECH AND MUSIC TRANSMISSION 12-27
audience, produced a whole-spectrum average pressure of 0.52 dyne per sq cm for a 3-ft
distance. The highest peak observed for the bass drum was 1250 dynes per sq cm. Thus
a range _of at least 68 db is indicated between the highest and lowest amplitudes in music.
The estimated range probably errs in the direction of being too small rather than too large.
12. TESTS OF SPEECH AND MUSIC TRANSMISSION
The performance of a system for the transmission and reproduction of speech or music
can be expressed in terms of objective measurements involving a determination of its
characteristics for steady-state sinusoidal waves of different frequency, or in terms of
subjective measurements involving the satisfaetoriness of the system from the viewpoint
of the person receiving the signals. This section is concerned with the subjective type of
measurement which involves, for speech, the recognizability and the naturalness of the
reproduced sounds, and for music, the emotional and esthetic properties of the reproduc-
tion. Measurements of this kind may be classed as laboratory and field measurements.
The former are particularly adapted to fundamental studies of the effects of various
physical factors on the reproduction; the latter, to evaluating performance under condi-
tions of actual use.
LABORATORY TESTS. The articulation test has come into wide use as a laboratory
method of measuring the recognizability of received speech sounds. One form of the test
which was used in obtaining the data given in the next article has been described by
Fletcher and Steinberg. In this form, a speaker utters the various speech sounds and an
observer writes down the sounds which he hears. The observed sounds are compared
with the called sounds, and the percentage of the called sounds that were correctly recog-
nized is obtained. This percentage is the articulation. To call the sounds, they are
combined in a random manner into syllables of the oonsonant-vowel-consonant type
which have no meaning in English. The syllables are spoken as parts of introductory
sentences, such as, "Please record the syllable ." The sounds used are those shown in
Table 1 (p. 12-20) , and they occur with uniform frequency in the testing lists. The per-
centage of the total number of spoken syllables which are correctly observed is called
the "syllable articulation." The "sound articulation" is the percentage of the total num-
ber of spoken sounds which are correctly observed. When attention is directed toward
a specific fundamental sound, e.g., b, the term "individual sound articulation" is used.
Similarly, "vowel articulation" is the percentage of the total number of spoken vowel
sounds which are correctly observed.
To obtain reproducible and representative results it is important that the testing crew
have normal voices and hearing and that they be thoroughly familiar -vrith the method.
The best number of voices and observers and the amount of testing material required
depend on the discrimination which is desired. For most of the data reported in the next
article, each of 8 callers reads a list of 66 syllables to 4 observers. Practice effects of two
kinds occur, a short-term period of improvement when the crew tests unfamiliar condi-
tions, and gradual long-term changes in skill. The first may be eliminated by repeating
tests; the second may be evaluated by suitable control tests on reference circuits. The
use of automatic equipment to facilitate the control of variable factors is very advanta-
geous, particularly when considerable testing is done. Castner and Carter have described
equipment of this kind. The sounds that the observer hears are recorded, and the re-
corded result is analyzed into various articulation values, automatically within a few
seconds after the test is completed, by suitable selecting and recording equipment. In
addition, various circuit conditions to be tested are set up at the proper time, the talking
levels of the callers are measured, and numerous other steps in a test are accomplished
automatically.
Another type of test that has been used somewhat is the "intelligibility test." In some
such tests, short sentences of the interrogative or imperative form containing a simple
idea are used. The sentences are considered to be understood if the observer either
records the sentence or records an intelligent answer. In others, English words, selected
at random from print, are used. The "discrete sentence intelligibility" is the percentage
of the total number of called sentences which are correctly understood. Similarly, the
"discrete word intelligibility" is the percentage of called words correctly observed. Fig-
ures 3 and 4 illustrate the types of relations between these intelligibilities and syllable
articulation. The intelligibility tests are useful in testing very poor systems having an
articulation of only a few per cent, which are used sometimes in fundamental studies.
Articulation and intelligibility tests afford a quantitative measure of the intelligibility
of reproduced speech. The naturalness of speech and music, and the emotional "and
esthetic appeal of musical sounds, are less definite, and have been studied principally by
12-28
ACOUSTICS
means of the AB judgment test. In this test, the observer listens to two conditions A
and B, and judges which condition is distorted, or which condition is the poorer etc.,
depending on the study. Sometimes one condition may be the original sound and the
80
e 60
20
20
so
100
FIG. 3.
40 60
Syllable Articulation
Discrete Sentence Intelligibility vs. Syllable Articulation
other condition the repro-
duced sound. Although such
tests do not always give a
quantitative measure of the
effects of distortion on natu-
ralness, esthetic appeal, etc.,
they do afford a means of
measuring the just-noticeable
amounts of distortion. This
type of test was used in stu-
dies on the audible frequency
ranges of music, speech, and
noise which have been re-
ported by Snow.
FIELD TESTS. The re-
sults of such laboratory tests
cannot be taken to indicate
directly the performance of
actual circuits under service
conditions. In service, there
is a wide range of variation in
a number of conditions, such
as the subject matter of con-
versations, the manner in
which the transmitter is spo-
ken into, the way in which the
receiver is held to the ear, and
the reactions of telephone users to the various circuit conditions. Because it is difficult
to specify definitely such conditions and hence simulate them in the laboratory, the repeti-
tion test, which has been described by Martin, has come into use. In this test, observations
are made on telephone circuits under service conditions. Essentially, the test is that of
noting the repetitions in a
telephone conversation and 10°
from a number of observa-
tions determining the repe-
tition rate. Martin's paper
describes repetition obser-
vations on conversations be-
tween several hundred sta-
tions in the American Tele- £
phone and Telegraph Com- ~
pany headquarters building =
and a similar number of sta- j=
tions in the Bell Telephone |
Laboratories building. To 5
provide data for rating *•
transmission performance, J
the station instruments and &
the transmission character-
istics of the interconnecting
trunks were varied and the
effects on repetition rate de-
termined. McKown and
Emling have described a
system of effective trans-
mission data for rating tele-
phone circuits, based on the
results of such tests and
articulation tests
OTHER TESTS. During the war a numbe
P
20
40 60
Syllable Articulation
FIG. 4. Discrete Word Intelligibility vs. Syllable Articulation
of new tests were devised for testing
speech transmission under conditions obtaining in military operations. See: Transmission
and Reception of Sounds under Combat Conditions, Miller and Weiner, Columbia University
Press, New York, 1948.
EFFECTS OF DISTOETION ON SPEECH AND MUSIC 12-29
PREDICTION OF ARTICULATION TEST RESULTS. On many types of speech-
transmission circuits it is possible to measure the circuit characteristics and noise levels
and by means of these data compute the articulation score that would be obtained. Com-
putational methods are also useful hi the design of equipment for speech circuits and of
considerable theoretical interest in the study of the interpretation of speech sounds.
See: Beranek, L. L., Design of Speech Communication Systems, Proc. IRE, Vol. 35, SO
(1947); French and Steinberg, Factors Governing Intelligibility of Speech Sounds, /.
Acous. Soc. Am., Vol. 19, 90 (1947); and Fletcher and Gait, The Perception of Speech and
Its Relation to Telephony, /. Acous. Soc. Am., July 1950.
BIBLIOGRAPHY
Bureau of Publications, Bell Telephone Laboratories, High Speed Motion Pictures of the Human
Vocal Cords. (Two reels of slow-motion views available for loan on request.)
Castner and Carter, Developments in the Application of Articulation Testing, Bell Sys. Tech. J., July
1933, p. 34 /.
Crandall, I. B., Sounds of Speech, Bell Sys. Tech. J., October 1925, p. 5S6.
Dudley, H., Remaking Speech, J. Acous. Soc. Am., Vol. 11, 169 (October 1939).
Dudley, H., The Carrier Nature of Speech, Bell Sys. Tech. J., Vol. 19, 495 (October 1940).
Dudley, Homer, and Otto O. Gruenz, Jr., Visible Speech Translators with External Phosphors, J.
Acous. Soc. Am., Vol. 18, 62 (July 1946).
Dunn, H. K., and D. W. Farnsworth, Exploration of Pressure Field Around the Human Head during
Speech, /. Acous. Soc. Am., Vol. 10, 184 (January 1939).
Dunn, H. K., and S. D. White, Statistical Measurements on Conversational Speech, J, Acous. Soc.
Am., Vol. 11, 278 (January 1940).
Firestone, F. A., Artificial Larynx for Speaking and Choral Singing, J. Acous. Soc. Am., January 1940,
p. 11.
Fletcher, H., Physical Characteristics of Speech and Music, Bdl Sys. Tech. J., July 1931, p. 349.
Fletcher and Steinberg, Articulation Testing Methods, Sett Sys. Tech. J., October 1929, p. 806.
French, Carter, and Koenig, Words and Sounds of Telephone Conversation, Bell Sys. Tech. J., April
1930, p. 290.
Koenig, W., H. K. Dunn, and L. Y. Lacy, Sound Spectrograph, J. Acous. Soc. Am., Vol. IS, 19 (July
1946).
Kopp, G. A., and H. C. Green, Basic Phonetic Principles of Visible Speech. J. Acous. Soc. Am., Vol.
18, 62 (July 1946).
Lewis, Don, Vocal Resonance, J. Acous. Soc. Am., VoL 8, 91 (October 1936).
Lewis and TutMll, Resonant Frequencies and Damping Constants, J. Acous. Soc. Am., VoL 11, 451
(April 1940).
Martin, W. H., Rating the Transmission Performance of Telephone Circuits, BeU Sys. Tech. J., Janu-
ary 1931, p. 116.
McKown and Emling, A System of Effective Transmission Data for Rating Telephone Circuits, BeU
Sys. Tech. J., July 1933, p. 331.
Paget, Sir Richard, Production of Artificial Vowel Sounds, Proc. Roy. Soc., VoL 102, 752 (1923).
Potter, R. K., Visible Patterns of Sound, Science, VoL 102, 463 (Nov. 9, 1945).
Potter, R. K., G. A. Kopp, and H. C. Green, Visible Speech. Van Nostrand (1947).
Riesz, R. R., An Artificial Larynx, J. Acous. Soc. Am., January 1930, p. 273.
Riesz, R. R., and L. Schott, Visible Speech Cathode Ray Translator, J. Acous. Soc. Am., Vol. 18, 50
(July 1946).
Sacia and Beck, Power of Fundamental Speech Sounds, BeU Sys. Tech. J., July 1926, p. 393.
Sivian, L. J., Speech Power and Its Measurement, Btll Sys. Tech. J., October 1929, p. 646.
Sivian, Sunn, and White, Absolute Amplitudes and Spectra of Musical Instruments and Orchestras,
J. Acous. Soc. Am., January 1931, p. 330.
Steinberg, Application of Sound-measuring Instruments to the Study of Phonetic Problems, J. Acous.
Soc. Am., July 1934, p. 16. _ ,
Steinberg, J. C., and N. R. French, The Portrayal of Visible Speech, J. Acous. Soc. Am., VoL IS, 4
(July 1946).
Stewart, J. Q., An Electrical Analogue of the Vocal Organs, Mature, September 1922, p. 311.
Wolf, Stanley, and Sette, Quantitative Study of the Singing Voice, J. Acous. Soc. Am., VoL 6, 255
(April 1935).
EFFECTS OF DISTORTION ON SPEECH AND MUSIC
By John C. Steinberg and W. A. Munson
In studies of the effects of distortion, it is desirable to have a suitable reference system.
Under certain conditions, air transmission from speaker to observer approaches such a
reference. Owing to practical difficulties in changing and controlling an ah- transmission
system, it is convenient to use electrical systems composed of transmitters, amplifiers,
and receivers or loudspeakers. By suitable calibration and equalization, such systems
can be made to approach air in transmission properties, and various amounts of degrada-
tion or improvement can be introduced. Circuits of this type have been studied by means
of articulation and judgment tests and the effects of various kinds of distortion de-
termined.
12-30
ACOUSTICS
13. EFFECT OF FREQUENCY DISTORTION
AUDIBLE FREQUENCY RANGES OF MUSIC, SPEECH, AND NOISE. One step
in the evaluation of the effects of distortion on the interpretation of sounds is the deter-
mination of the just-noticeable amounts of distortion. Snow has reported the results of
tests on the lower and upper frequency limits of various types of sounds. The sounds
as produced in one room were picked up by a microphone and transmitted to a second
room where they were reproduced by means of loudspeakers. By means of filters, all
frequencies above or below any desired cutoff could be suppressed. By comparing the
unfiltered with the filtered transmission, trained observers determined the just-detectable
upper and lower cutoffs. The results of the tests are shown in Fig. 1. The ends of the
Audible Frequency Range
for Music Speech and Noise
- Actual Tone Range
nilWIIIIIltl Accompanying Noise Range
°- Cut-off Frequency of Filter
Detectable in 80% of Tests
Bass Drurn-
\
BflHW
HUH
p
Jii
Bass Viol
nit
Ce|l0 .
•( HffHJWJWI
Violin
HIK
nun
Trombone
F ench Ho
n o n—
in n
Bass Saxophone
it
laiiiiiiiui
Bass CtaE&Lfit
Clarinet
j J
Sopramo Swfophofle—
Oboe
' "
'
Flute
Male Speech- -
Female Speech
°"
Key JiQgUng-— — —— —
0
4
0
100 500 1,000 5,000 10,000 20,
Frequency In Cycles per Second
4 5 6 7 8 9 10
Frequency Level in Octaves from 16.35 Cycles
FIG. 1. Audible Frequency Ranges
lines representing the audible ranges are the cutoffs where the correct judgments amounted
to 60 per cent. Circles mark the cutoffs where 80 per cent correct judgments were ob-
tained The ^ musical sounds produced by many of the musical instruments were accom-
panied by noise such as key clicks, lip noises, "buzz" of reeds, and hissing of air. As far as
possible, the observers tried to distinguish between tone and noise. The lines indicate
their decision as to the actual tone range, and the short vertical lines indicate the noise
range. In all cases, the upper frequency limit exceeds very greatly the frequencies of the
Highest notes that the instruments were capable of producing. Except for the piano the
^
ad
Uonal type of test was made with music furnished by an 18-pieoe orchestra. In this test
the filtered reproduction was always presented on the B condition, and the unfiltered on
the A condition. The observers were asked to rate the quality of the B condition as a
percentage of the A condition. A ratmg of less than 100 per cent indicated a degradation;
Lrr^l th*T th*JV100.Per ce°* ******* an improvement. The various Sitoffs oc^
cm-red on the , B condition m random order. The results of this test are given in Fig 2
The judgment of the ten observers taking part in this test was that the quality ^creased
rapldly as the cutoff was extended upward to 8000 cycles or downward to 80 cycles
AKTICULATION TESTS
12-31
The results, in view of the nature of the test, were surprisingly consistent. In only about
3 per cent of some 400 observations was the quality of a filtered system given a rating
greater than 100 per cent, so that, in general, the reproduction of the full audible range
was preferred.
20
90
80
n
3
High Pass Filters
n First Test (Blue Danube)
o Second Test (In a Village)
1 \ \
&T_
i
ill
i^°
70
^60
J-50
CO
0-40
30
20
10
x
Low Pas:
& Firs
c Sec
niters
tTest
and Test
I/
O.r
\
/J
\
i
i
^
i
\
.
i
\
/
'j
A
\
s 1
r^
j
1ft*
O.
|
50 100
500
Cut-off Frequency :n Cycles per Second
FIG. 2. Orchestral Quality vs. Cut-off Frequency
5000 100OO 200QO
14. ARTICULATION TESTS
RELATION BETWEEN ARTICULATION AND LEVEL OF SPEECH ABOVE
THRESHOLD. The articulation test affords a means of dealing with the effects of dis-
tortion in a more quantitative way than does the judgment test. An extensive series of
articulation studies have been reported by Fletcher and Steinberg, for widely varying
types of distortion. Figure 3 shows the effect, on syllable articulation, of changing the
received speech level (see also article 31). In the range from 10 to 40 db above threshold,
the articulation increases rapidly with increasing level. In the range from 50 to 90 db
there is little change with increasing level. Experimentally it has been determined that,
if a speaker radiates the average speech power of 10 microwatts, a listener of normal hear-
100
"r
20
40 60
DB above Threshold
FIG. 3. Effects of Speech Level on Syllable Articulation
ing 1 meter away in the undisturbed sound field will "hear the speech at a level of about
62 db above threshold. Figure 3' shows that this level is sufficient to insure very good
articulation. It is a level that would obtain in conversing at a meter's distance in a cpiiet,
well-damped room. A more detailed picture of the effects of speech level on articulation
12-32
ACOUSTICS
60
40
20
. Phonetic Power
DB from lO^Watt
- Long Vowels 113
— Short Vowels 113
— Nasal Cons. 106
Stop Cons. 98
Fricative Cons. 99
is obtained by grouping the sounds into five groups, where the sounds in each group have
somewhat similar properties. The grouping used is: long vowels — a, a, e, o, o', u; short
vowels — a', e, i, o, u, w, y; nasal
consonants — I, m, n, ng, r\ stop con-
sonants— 6, ch, d, g, h, j1, k, p, t;
fricative consonants—/, s, sh, $t, th,
thf (then), v, z, zh (see Table 1, p.
12-20). Figure 4 shows the group
articulation vs. speech level. As
the level is increased from thresh-
old, the vowels are the first to be
recognized and are followed in order
by the nasal, stop, and fricative
consonants. The apparent differ-
ences between the levels of the
sound groups, as judged from artic-
ulation tests, correspond approxi-
mately with the differences in av-
erage phonetic powers shown in
the insert. For example, the vowel
articulation at a level of 25 db is
about 90 per cent. The nasal con-
sonant group must be increased 6
db from the 25-db level for an ar-
ticulation of 90 per cent, and the
stop and fricative consonants must
FIG. 4. Effects of Speech Level on Sound Articulation be increased by 10 and 13 db, re-
spectively.
EFFECT ON ARTICULATION OF REMOVING PORTIONS OF THE SPEECH
FREQUENCY RANGE. To determine the effects of frequency distortion on articula-
tion, electrical filters were introduced into a circuit that was otherwise reasonably free
from distortion. One type of filter (low-pass filter) eliminated all components above a
chosen cutoff frequency and uniformly transmitted the remainder of the range. Another
type (high-pass filter) eliminated all components below a chosen cutoff frequency. Fig-
ure 5 shows the effects on articulation of changing the cutoff frequency of these filters.
The level of the speech, before the filter was introduced, was held constant at 70 db above
threshold. The curves marked L.P. are for the case where components below the cutoff
frequency were transmitted; for the H.P. curves, components above the cutoff frequency
were transmitted. The cutoff frequency at which the L.P. andr H.P. curves intersect is
/v
20
40 60
DB above Threshold
100
H
P.
"""""^
^
LJP.
/
C
Stop
ons.A
rf.
II
HJ
P-
*7f
L.P.
It
/
/
/
Fricat'i
Cons. A
/e
1
1Q2 2 4 68io3 2 4 68 4 ~22~
Cut-off Frequency
FIG. 5. Articulation vs. Cut-off Frequency
a frequency such that the frequency range below it has an articulation equal to the fre-
quency range above it. This intersection frequency is always higher for female than for
male speech, indicating that the higher-frequency ranges are more important for female
speech. The frequency range in which the curves bend down is the range of importance
in articulation, which as may be seen varies from one sound group to another P
ABTICULATION) TESTS
12-33
^ EFFECTS OF AN EXTRANEOUS NOISE ON ARTICULATION. As pointed out
in the article on masking, noise has the effect of shifting the threshold of audibility of
other sounds heard in the presence of noise. If the masking of a noise is reasonably
uniform over the important speech frequency range, articulation tests made in the presence
°^ nCf^j °^ the main eSect * to shift the curves of articulation vs. level above
threshold. Figure 6 shows articulation vs. level for a quiet circuit and for the circuit with
noise present at three different levels. The corresponding masking effects of the noise
are shown by the insert (noise audiogram). The abscissa of the articulation vs, level
curves gives the decibels above threshold of the speech on a quiet circuit. The amounts
of the shift in the articulation curves correspond reasonably well with the average amounts
of masking produced by the noise. When both the speech and noise levels are high, the
100
Eflect of Noise on Articulation
20
40
100
50 80
DB Above Threshold
FIG. 6. Effects of Noise on Articulation*
observed articulation values are less than would be indicated by a simple shift in the
articulation-level curves. Modulation between the speech and the noise then takes place
in the ear, which decreases the maximum value of articulation that can be obtained.
When the masking is confined to a limited portion of the speech frequency range, such as
that produced by a 2000-cycle tone, the effects on articulation cannot be represented by a
simple shift in the articulation vs. level curves. In this ease, the curves are both shifted
and changed in shape. Moderate amounts of deafness affect articulation in much the
same way as noise. When the hearing loss is uniform with frequency, the articulation
to be expected is that obtained by a corresponding shift in the normal articulation vs.
level curve.
EFFECT OF RESONANCE TYPE OF FREQUENCY DISTORTION ON ARTICU-
LATION. A very common type of distortion occurring in transmission systems is that
of resonance. Figure 7 shows the effects of a resonant peak at 1100 cycles, on articulation.
The left-hand eurves, numbered 2 and 3, show the loss in decibels at each frequency
relative to the loss in the uniform system designated as 1. The right-hand curves show
articulation vs. level for the three systems. The abscissa is the decibels above threshold
of the normal speech, i.e., before inserting the resonance distortion. At the lower speech
levels the decrease in articulation due to the distortion is much greater. Most of the
articulation loss for a resonance type of distortion appears to arise because those sounds
which have then- important components in the frequency ranges removed from resonance
axe received at effectively lower than normal levels. For example, a large part of the
important frequency range for fricative consonants is received at a level some 30 to 40 db
below normal in curve 3. When the normal level is low, this further reduction causes
appreciable articulation losses. Although the articulation at optimum received levels may
not b£ seriously affefrt&l by resonance distortion* the tonal character or naturalness of tfee
distorted sp^ecfe is appreciably impaired.
12-34
0
10
CQ20
Q
c
ACOUSTICS
1
|\
^
^**
X
*-
^
/
' \
80 —
y
/
/
,
7
S
S.
c
/a
/
/
2,
'
\
s
s,^
- — fe
J
/
/
_^-1
S
/ \
v
V,
*vs
<£
1
/
3/
L
40
50
1
/
\
/
)>
\
/
,s
/
'
\
/
^"
s^
s.
k
s
S.
2 345789, 2 34567 89 4 40 50 S(
O2 103 104 DB above Threshold
Frequency of Normal Speech
FIG. 7. Effects of Resonance Type of Frequency Distortion on Articulation
EFFECTS OF NON-LINEAR DISTORTION ON ARTICULATION. Non-linear dis-
tortion arises when the output of a system is not proportional to the input. There are
two cases of interest: (a) when the output increases at a more rapid rate than the input;
(6) when the output increases at a slower rate than the input. In both, modulation
products or extraneous frequencies are introduced for the intense sounds when they cover
an appreciable part of the curved portion of the input vs. output characteristic. The
result is a decrease in the articulation of such sounds. The amount of the decrease de-
pends upon the amount of the curvature. In addition, in (a) the intense sounds are
amplified relative to the faint sounds, which has the effect of decreasing the articulation
of the faint sounds. In (b) the faint sounds are amplified relative to the intense sounds.
This has the effect of increasing the articulation and may, if the received speech level is
below the optimum receiving level, offset the decrease due to modulation effects. For
optimum receiving levels, however, the net result is always a decrease in articulation when
the system is free from noise.
EFFECTS OF CLIPPING ON ARTICULATION. Articulation tests that have been
made with voice-operated relays give an indication of the importance to articulation of
Initial Consonant Articulation h
M row-^oiQivjcoioc
o o ooooooo_oc
Is*
^3,
^v
X
rx
X
X
\
x
\
Vo
\
0 0.02 0.04 0.06 O.C
Interval of Time Cljpped from Initia
38 0.10 0.12
Consonant in Seconds
0.1
FIG. 8. Effect of Clipping an Element of Time from Speech Sounds
initial portions of the duration intervals of speech sounds. In the tests, syllables of the
consonant-vowel-consonant type were spoken at intervals of about 3 sec. A circuit
having a relay adjusted so as to break contact almost simultaneously with the beginning
ARTICULATION TESTS
12-35
90
n
80
/
~
i
fa
70
w
S
t,
f
s
s,
5 60
/
*
N,
J
^
° 50
/
s
N,
S 40
^
>
t
30
/
/
20
J
f
10
n
Frequency Multiplication Factor
FIG. 9. Effect on Articulation of Multiplying Frequencies
by a Constant Factor
of a syllable was used. The contacts
of a second relay formed a short cir-
cuit across the receiver. The oper-
ation of the first relay caused the
second relay to break contact after
an interval of time depending on the
time constants of the relay circuit
alone. The time taken for the sec-
ond relay to operate represents the
time clipped from the initial con-
sonants of the syllables. Figure 8
shows the initial consonant articula-
tion plotted against the operating
time of the second relay. The data
indicate that equal elements of time
in the duration intervals of the
sounds were of equal importance to
the average articulation. For ex-
ample, the average duration time of
the initial consonants in these tests
was about 0.16 sec. When a time interval of 0.08 sec was clipped from the sounds, the
articulation was decreased by a factor of about 50 per cent.
EFFECTS OF FREQUENCY SHIFT ON ARTICULATION. One type of frequency
shift, namely, the multiplication
of frequencies by a constant fac-
tor, occurs when the speed of a
sound film or phonograph turn-
table during reproduction is dif-
ferent from the speed used during
recording. The effect of this type
of distortion on articulation is
shown in Fig. 9. Another type,
the addition or subtraction of a
constant number of cycles to all
frequencies, occurs when the fre-
quency of the carrier at the mod-
ulating end differs from that at
the demodulating end of a carrier
Frequency Shift " system. The effect of this type
Fia. 10. Effect of Frequency Shift on Articulation of shift is shown in Fig. 10. In
general, the decrease in articula-
tion is greater when the frequencies are shifted to lower values than when they are shifted
toward higher values. In the first type of distortion the duration of the sounds is
changed, whereas in the second type the duration is unchanged. In the first type the har-
monic relationship is maintained, whereas in the
second type this relationship is not preserved. In
order to interpret speech sounds perfectly it seems
to be necessary to preserve both these properties.
EFFECTS OF PHASE DISTORTION ON AR-
TICULATION. The aspect of phase distortion that
has received most attention is the so-called "delay
distortion" which arises when the phase characteris-
tic of a transmission system is not proportional to
1UU
90
80
70
|60
•550
.«
S40
30
20
10
°3
/
""•s
\,
/
x|
\
^
S*
"V,
^v
-*"
^"x,
^s.
•^
I
3ow
iwar
d
Upv
fard
00 200 100 0 100 200 3OO 400 5C
frequency but is of the type shown by the curved £
line in Fig. 11. This type is of interest because it •=
Fig. __-
occurs in loaded lines and in low-pass niters. The
delay distortion (see Section 5, article 9) is the ^dif-
ference between the slope of the phase characteristic
at any frequency / and the minimum slope, and is
usually expressed in the form
(*J\ - (*£}
\du/f VSoj/
where £ is the phase shift in radians and w = 2irf. ~2
The approximate effect of this type of distortion is FIG. 11. A Curved Phase Characteristic
12-36
ACOUSTICS
Non-Delayed Band 0-3000
Delayed Band 3000-4500
100
E— £L
0 .04
.08 .12 .16 .2
Non -Delayed Band 0-2000
Delayed Band 2000-4500
Non-Delayed Band O-1500
Delayed Band 1500-4500
to delay the frequency com-
ponents near /, with respect
to those components in the
range of minimum slope, by
the amount of the delay dis-
tortion. The effects on ar-
ticulation of delaying various
portions of the speech fre-
quency range are shown in
Fig. 12. In these tests, a
nominal undistorted speech
frequency range of 0 to 4500
cycles was divided into two
parts by means of niters and
each part transmitted through
a different channel. After
transmission the two parts
were recombined. The phase
characteristic of each channel
approximated a straight line
over the greater part of the
frequency range. The slope
of the characteristic of one
channel could be increased by
various amounts over that of
the other channel. One chan-
nel thus introduced a definite
time delay, in the sense used
here, with respect to the other
channel, i.e., a delay given by
the difference in the slopes of
their phase characteristics.
The articulation values de-
crease with increasing delay
and approach the articulation
of the more intelligible band
which was also the least-
delayed band.
To determine the effects on
articulation of delay distor-
tion which varied continu-
ously with frequency, a sys-
tem having the delay-distor-
tion characteristics shown in Fig. 13 was studied. These characteristics were obtained from
network sections of the all-pass type. By using different numbers of sections, different
amounts of delay distortion could be obtained. The attenuation characteristics of the
networks were equalized to
2500 cycles, and a 2400-
cycle low-pass filter having
negligible phase distortion
was associated with the net-
works. Figure 14 shows the
effect of the delay distortion
on articulation.
To study the effects of de-
lay distortion at higher fre-
quencies, articulation tests
were made on a system con-
taining first one, and then
twenty-five, 5000-cycle low-
pass filters in series. In both
cases, the attenuation was
equalized to 5000 cycles. " o 400 800 1,200 i,eoo 2,000 2,400 2^800
The delay-distortion char- Frequency In Cycles per Second
a^fceristics and the results of Fro. 13. Delay Distortion for an All-pas* Network
Non-Delayed Band 750-4900
Delayed Band 0-750
LUU r
H
<j
L
.L
Art!
Non-C
:ulat1o
delayed
I Of/
Band
0 .04 .08 .12 .16 .2
Time of Delay In Seconds
FIG. 12. Effects of Delay on Articulation
ARTICULATION TESTS
12-37
the tests are shown in Fig. 15. Because the component frequencies near the cutoff are
delayed by phase distortion of this type, they fail to contribute their normal amounts to
the total articulation carried by the unattemiated frequency band. Thus the distortion
has the effect of reducing the transmitted frequency range, 'so that the effective trans-
mitting range depends upon both the phase and the attenuation characteristics.
Sound Articulation M
00 00 <O U> O
o 01 o 01 o
— —
-£-.
~" •
• II.
sfe.
o
3 4 8 12 16 20 24 21
Number of Sections
FIG. 14. Articulation vs. Delay Distortion
AUDIBLE EFFECTS OF PHASE DISTORTION. Quite aside from the effects on
articulation, when speech from a system having phase distortion is compared with that
from a system of negligible distortion, it is noticed that the distorted speech is axicom-
panied by certain audible effects which appear to be extraneous to the speech and transient
in character. These effects, which are due to components of different frequencies arriving
at different times, are often termed "birdies" or **tweets," for delay distortion of the type
shown above. Their noticeableness depends upon the amount of delay distortion and
the frequency range in which it occurs. For speech, it was found that one section of the
all-pass network, when associated with a 2400-cycle low-pass filter, had sufficiently small
delay distortion so as to be just noticeable. This determination was made by alternately
listening to speech from the system under two conditions: one, the filter alone; two, the
0.014
CL012
0.008
0.006
0.002
1 I I < jOrte Filter ;
Observed Sound Articulation 98.4
5 Fitters f 25 Fffiets
97.8
Ll5 Ftters
10 Flters
1,000
5,OOO
2,000 3,000 4,000
Frequency in Cycles per Second
FIG. 15. Articulation and Delay Distortion for 5000-cyde Lew-pass Filters
filter with the aft-pass network. Judgments of which condition contained the network
were correct about 50 per cent of the time and wrong about 50 per cent of the time for
one section of the network. The total delay distortion at the cutoff frequency in this
case, i.e., that due to the filter plus that due to one section of the network, was about
0.006 see. When three seefcicms were used the distortion was easily noticed.
12-38
ACOUSTICS
Similar tests with the 5000-cycle low-pass filters indicated that some number between
5 and 10 filters in tandem would cause just-noticeable distortion and that the Distortion
was clearly noticeable for 20 filters in tandem. The amount of delay distortion at the
cutoff frequency for 5 filters is about 0.003 sec, and for 10 niters about 0.006 sec
The above figures depend somewhat upon the attenuation characteristic as the cutoff
frequency is approached, small amounts of attenuation reducing the noticeability of the
effects. The figures also vary somewhat with individuals, depending upon their experi-
ence and hearing characteristics.
Tests on piano reproduction when single notes were struck or when a passage of music
was played indicated that the distortion caused by 25 of the 5000-cycle low-pass filters in
tandem was not noticeable. As in speech, it would be expected that the noticeableness
of the distortion would depend upon the frequency range in which it occurs. In general,
the effects of delay distortion on music are very much less noticeable than on speech,
which is probably due in part to the more sustained character of music.
EFFECTS OF ROOM REVERBERATION ON ARTICULATION. To determine the
effects of room reverberation on articulation, the microphone of a system substantially
100
100
90
100
90
a I Cons«. Art-
Stop
468
468
468 24 2468
0.1 1.0 10 0.1 1.0
Distance from Transmitter- Ft.
FIG. 16. Effect of Reverberation on Articulation
free of distortion was placed in a room having variable reverberation conditions. The
room dimensions were 20 ft by 30 ft by 15 ft. The reverberation time was practically
uniform over the important speech frequency range. The articulation tests were made
under three conditions of reverberation, corresponding to the reverberation times 1.2, 2.2,
and 4.0 sec, and for the following four distances between the diaphragm of the microphone
and the lips of the speaker, 0.12 ft, 0.66 ft, 3.0 ft, and 15 ft. In aU the tests, the speaker
faced toward the microphone. Observers listened in another room, by means of head
receivers, to the speech picked up by the microphone in the reverberant room. A volume
indicator was used to measure the level of the speech from the microphone. The instru-
ment measures, substantially, the phonetic power of the vowel sounds. The gain of the
system between microphone and receiver was set so that the level of the speech received
by the observers, for the close. talking condition, was 74 db above threshold. The gain
of the system was then kept constant for all tests. The loss in speech level vs. distance
between microphone and speaker, and the articulation results, are shown in Fig. 16. The
speech level decreased inversely as the square of the distance for distances up to 1 ft from
the transmitter, but at the 15-ft distance the level was some 12 db greater than the level
obtained by assuming the inverse square relation. The solid curves designated as "sys."
ACOUSTIC PROPERTIES OF ROOMS 12-39
show articulation vs. distance between speaker and microphone, for the system alone.
They are graphs of the data of Figs. 3 and 4, where level above threshold has been con-
verted into distance between speaker and microphone. This was done by means of the
solid curve showing loss in speech level vs. distance, and taking the level for zero loss as
£ t 6 threshold- This level is, of course, some 20 db less than the level the observer
would have received if the speaker had spoken directly into his ear from a distance of 0. 12 ft.
A comparison of the curves indicates that the various sound groups were not uniformly
attenuated by increasing the distance between speaker and microphone. For a given
distance, the effect of increasing the reverberation time was always in the direction of
decreasing the articulation, even though the received speech levels increased as the rever-
veration increased. For distances up to 15 ft, at least, the articulation was appreciably
less for a reverberant room than it would be for one with perfectly absorbing walls.
15. AUDITORY PERSPECTIVE
Part of the emotional and esthetic appeal of sounds, when listened to directly with both
ears, may be ascribed to the appreciation of their spatial character. When this property
of sound waves is preserved in reproduction, the sounds are said to be reproduced in true
auditory perspective. Ideally, there are two ways of accomplishing such reproduction.
One is binaural reproduction, which aims to reproduce in the distant listener's ears, by
means of head receivers, exact copies of the sound waves that would exist in his ears if he
were listening directly. In this case, a complete system consisting of microphone, line,
and receiver is used for each ear. The other method uses loudspeakers and aims to repro-
duce in the distant hall an exact copy of the pattern of sound vibration that exists in
the original hall. In the limit, an infinite number of microphones and loudspeakers of
infinitesimal dimensions would be needed. In a symposium on reproduction in auditory
perspective the basic requirements for the production of orchestral music were discussed
and a practical system designed to achieve auditory perspective was described (Bell
Sys. Tech. J., April 1934).
BIBLIOGRAPHY
Auditory Perspective, a collection of six papers, BeZZ Sys. Tech. J"., April 1934, p. 239.
Fletcher, An Acoustic Illusion TelephonicalLy Achieved, BetL Lab. Rec., June 1933, p. 286.
Gait, R. H.f Noise Out-of-doors, J. Acous Soc. Am., July 1930, p. 30.
Snow, W. B., Audible Frequency Ranges of Music, Speech, and Noise, J. Acous. Soc. Am., July 1931,
p. 155.
Steinberg, J. C., Effects of Distortion on the Recognition of Speech Sounds, J. Aco-u*. Soc. Am., October
1929, p. 121.
Steinberg, J. C., Effects of Phase Distortion on Telephone Quality, Bdl Sys. Tech. J.t July 1930, p. 550.
Steinberg and Snow, Auditory Perspective and the Physical Factors Affecting It, BeU, Sys. Tech. J.,
April 1934, p. 245.
Tucker, R. S., Noise in Buildings, J. Acous. Soc. Am., July 1930, p. 59.
ACOUSTIC PROPERTIES OF ROOMS
By Vern O. Knudsen
The acoustic quality of nearly all communication systems, as radio, television, teleph-
ony, motion pictures, phonograph recording, hearing aids, and public-address and other
sound-amplifying or -reproducing systems, is largely influenced by the acoustic properties
of the rooms in which the sound to be transmitted or recorded is generated, and in which
this sound is reproduced.
The following definitions pertinent to the acoustic properties of rooms have been selected
from American Standard Acoustical Terminology — Z24.1-1942-(see J. Acous. Soc. Am.,
Vol. 14, 84-110 [1942] for these and other pertinent definitions).
Effective Sound Press-ore (P). The effective sound pressure at a point is the root
mean square value of the instantaneous sound pressure over a complete cycle, at that
point. The unit is the dyne per square centimeter.
Pressure Level.* The pressure level, in decibels, of a sound is 20 times the logarithm
to the base 10 of the ratio of the pressure P of this sound to the reference pressure PQ. Un-
less otherwise specified, the reference pressure is understood to be 0.0002 dyne per sq cm.
* In discussing sound measurements made with pressure or velocity microphones, especially _ in
and the pressure or velocity is generally unknown.
12-40 AOOWSTICS
Velocity Level.* The velocity level, in decibels, -of a sound is 20 times the logarithm
to the base 10 of the ratio of the particle velocity of the sound to the reference particle
velocity. Unless otherwise specified the reference particle velocity is understood to be
5 X 10"6 cm per sec effective value.
Sound Energy Density (£). Sound energy density is the sound energy per unit volume.
The unit is the erg per cubic centimeter.
Sound Intensity * (/). The sound intensity of a sound field in a specified direction
at a point is the sound energy transmitted per unit of time 'in the specified direction through
a unit area normal to this direction at the point. The unit is the erg per second per square
centimeter, but sound intensity may also be expressed in watts per square centimeter.
Intensity Level * (/£>. The intensity level, in decibels, of a sound is 10 times the
logarithm to the base 10 of the ratio of the intensity / of this sound to the reference in-
tensity /o. Unless otherwise specified the reference intensity J0 shall be 10 16 watt per
sq cm.
Echo. An echo is a wave which has been reflected or otherwise returned with suffi-
cient magnitude and delay to be perceived in some manner as a wave distinct from that
directly transmitted.
Multiple Echo. A multiple echo is a succession of separately distinguishable echoes
from a single source.
Fhrtter Echo. A flutter echo is a rapid succession of reflected pulses resulting from a
single initial pulse. If the flutter echo is periodic and if the frequency is in the audible
range it is called a musical echo.
Noise. Noise is any undesired sound.
Acoustic Reflectivity. The acoustic reflectivity of a surface not a generator is the
ratio of the rate of flow of sound energy reflected from the surface, on the side of incidence,
to the incident rate of flow. Unless otherwise specified, an possible directions of incident
flow are assumed to be equally probable. Also, unless otherwise stated, the values given
apply to a portion of an infinite surface, thus eliminating edge effects.
Acoustic Absorptivity. The acoustic absorptivity of a surface is equal to 1 minus the
reflectivity of that surface. (Sometimes called Sound-absorption Coefficient.}
Sabin. The sabin is a unit of equivalent absorption; it is equal to the equivalent ab-
sorption of 1 sq ft of a surface of unity absorptivity, i.e., of 1 sq ft of surface which ab-
sorbs all incident sound energy.
Acoustic Transmittivity. The acoustic transmittivity of an interface or septum is the
ratio of the rate of flow of transmitted sound energy to the rate of incident flow. Unless
otherwise specified, all directions of incident flow are assumed to be equally probable.
Reverberation. Reverberation is the persistence of sound, due to repeated reflections.
Rate of Decay (of Sound Energy Density). The rate of decay of sound energy density
is the time rate at which the sound energy density is decreasing at a given point and at
a given time. The practical unit is the decibel per second.
Reverberation Time (T), The reverberation time for a given frequency is the tune
required for the average sound energy density, initially in a steady state, to decrease,
after the source is stopped, to one-millionth of its initial value. The unit is the second.
Mean Free Path. The mean free path for sound waves in an in closure is the average
distance sound travels in the inclosure between successive reflections,
16. REQUIREMENTS FOR GOOD ACOUSTICS
In order that a room may have good acoustics it is necessary (1) that the sound be
sufficiently loud in the room; (2) that the room be free from noise whether of internal or
external origin; (3) that the room be free from echoes, "flutters," or other interfering
reflections; (4) that the reflecting boundaries of the room be so disposed as to provide a
nearly uniform distribution of sound energy throughout the room; (5) that the room be
free from undesirable resonance; and (6) that the reverberation in the room be sufficiently
reduced to avoid excessive overlapping or commingling of successive sounds of articulated
speech or music, but that the room be sufficiently "live" at all frequencies to give a pleas-
ing effect to either speech or music as judged by the average listener.
In order to attain these necessary conditions for good acoustics the architect and acousti-
cal engineer must assume responsibility relating to the following: (1) the selection of the
*Ia discussing sound measurements made with pressure or velocity microphones, especially in
imeJosures involving normal modes of vibration or in sound fields containing standing waves, caution
must be observed in using the terms "intensity" and "intensity leveL" Under such conditions the
teraaa * pressure level" or "velocity level" are preferable since the relaiaonsnip between the intensity
and the pressure or velocity is generally unknown.
GEOMETRIC AND WAVE ACOUSTICS 12-41
site; (2) the making of a noise survey in the proximity of the proposed site; (3) the selec-
tion ol a general type of wall and ceiling construction which will insulate the building
adequately against external noise and vibration; (4) the selection and arrangement of
rooms which require acoustical designing; (5) the design of the rough sketches for all
speech rooms, music rooms, recording or broadcasting rooms, based upon the requirements
for the proper distribution of direct and of reflected sound; (6) the application of appro-
priate formulas and principles to the detailed design of shape, sound insulation, and sound
absorption for^all rooms which require acoustical designing; (7) the selection of materials
which will satisfy the acoustical, structural, decorative, and economic requirements; (8)
the supervision of all aspects of construction which will affect the outcome in acoustics,
and^ especially the making of tests on such materials as acoustical plaster; and (9) the
testing of the completed building with regard to the distribution of sound; freedom from
echoes, sound foci, or interfering reflections; the optimal conditions of reverberation; and
the adequacy of sound insulation. In general, the acoustic problem consists of the ade-
quate reduction of noise and vibration, and the designing of interiors in which the voice or
instrumentation is heard or recorded most satisfactorily. All the factors mentioned in this
section relate to the problem of room acoustics. One of the most basic of these factors is
the problem of the growth and decay of sound in a room or, more strictly, the transient
and steady-state behavior of sound in that room. Before considering this problem, it will
be helpful to describe briefly two possible approaches to this and related problems: one,
geometric acoustics, and the other, wave acoustics,
17. GEOMETRIC AND WAVE ACOUSTICS
Geometric or "ray" acoustics, as applied to the acoustics of rooms, assumes that sound
travels in rays, that its frequency remains unchanged during the transient state as well
as the steady state, that the rays are reflected, with partial absorption and transmission,
at each encounter with the boundaries of the room, and that after a number of successive
reflections the sound in the room becomes diffuse (all directions of propagation being
equally probable) and of uniform energy density throughout the room. Obviously, this
oversimplifies the actual behavior of sound waves in the room, especially when the wave-
lengths of the sound, as is often the case, are not small compared with the dimensions of
the room; it neglects entirely such important properties as the normal modes of vibration
of the room, interference, and diffraction. In spite of these shortcomings, it leads to many
principles and formulas by means of which the acoustical engineer or architect can design
auditoriums with satisfactory acoustics.
Wave acoustics deals with sound as waves; it offers the only means of dealing rigorously
with wave phenomena in bounded spaces, with interference, diffraction, normal modes of
vibration, and with the influence of localized areas of absorptive material and of irregular-
ities of the contours of the boundaries of the room on both the transient and steady states
of the sound in the room. The difficulties in applying wave acoustics to rooms are so
great that very little progress has been made until recently, and even now much remains
to be done before it can be used effectively by the average architect or acoustical engineer.
Historically, the study of the acoustic properties of rooms began and has continued,
very largely, on the assumption that geometric acoustics is adequate to cope, at least
approximately, with the transient and steady-state behavior of sound waves in most rooms.
Obviously, the methods of geometric acoustics furnished satisfactory approximations in
rooms in which the ratio of the room dimensions to the wavelength of the sound is large
and in which the sound distribution is thoroughly diffuse (the "ergodic" state), but in
most rooms, and especially for sounds of low frequency, the more rigorous methods of
wave acoustics, recently developed by Morse and Bolt, should be used so far as this is
possible. (See Morse and Bolt, Sound Waves in Rooms, Remews «/ Modern, Posies,
April 1944). These methods of wave acoustics already have explained many apparent
anomalies in room acoustics, especially those relating to the absorptive properties of
acoustic materials as used in different rooms. No one who is not familiar with these
methods should undertake the design of a room in which good acoustics is a prime require-
ment. Unfortunately, the results of these studies are not yet sufficiently simplified to be
used by the average engineer as the basis for making routine analyses of the acoustic
properties of rooms. Fortunately, on the other hand, the approximate and much simpler
methods of geometric acoustics, when used with an understanding of the consequences
and modifications which wave acoustics entails, will be found to be satisfactory for making
the routine calculations which govern the acoustic properties of most rooms, such as offices,
restaurants, classrooms, and residential rooms. For the acoustic design of broadcasting
and motion-picture studios, auditoriums, theaters, churches, music rooms, courtrooms,
12-42 ACOUSTICS
lecture rooms, and all other rooms in which high-quality speech and music are required,
full use should be made of the methods of wave acoustics, as far as they are applicable.
For the present, the methods of geometric acoustics continue to be used by most engi-
neers for designing or correcting the acoustic properties of rooms, and their methods
probably will continue to be used for possibly another five to ten years, but they should
be used only in the light of existing and advancing knowledge of wave acoustics. In the
following treatment, based largely on geometric acoustics, the practical modifications
which wave acoustics imposes or suggests will be considered, and those who use this hand-
book as a guide for planning for good acoustics should give similar consideration to the
relevance of wave acoustics in modifying the calculations and conclusions based on geo-
metric acoustics.
18. GROWTH AND DECAY OF SOUND IN ROOMS-
GENERAL CONSIDERATIONS
The approximate theories in use today are based upon the assumptions that sound,
originating at some point in a room, propagates rays of vibratory energy with a speed of
about 1125 ft per sec, uniformly in all directions; that these rays are partially reflected
by the boundaries of the room; and that even after the source of sound is stopped these
rays persist with their original frequency but become feebler after each reflection until
ultimately they become inaudible. In these approximate theories it is assumed that the
sound energy persists in rays or bundles; that, during the decay, the sound energy in the
room remains constant in these rays or bundles for a short interval of time, equal to the
time required for a ray to travel the average distance between successive reflections, the
mean free path, and that then the total sound energy in the room suddenly drops a certain
amount determined by the "average" (usually the weighted arithmetical mean) acoustic
absorptivity of the boundaries of the room; and that this process of absorption by discrete
steps continues until all the sound energy is converted into heat.
Although most of the absorption takes place at the boundaries at low frequencies, the
absorption in the air at frequencies above 5000 cycles may be greater than the absorption
at the boundaries. If the source continues to generate sound at a constant rate, a condi-
tion of equilibrium will be reached in which the rate of supply of sound energy to the room
is just equal to the rate of absorption by the air and the boundaries. If the source is then
stopped the sound in the room will die away at a rate equal to the rate of absorption, which
is determined principally by the size, the shape, and the boundaries of the room. Although
this decay is strictly made up of the free, damped, normal modes of vibration of a three-
dimensional continuum, the decay is approximately represented by the simplification de-
scribed above, provided that the absorptive material is distributed throughout the bound-
aries of the room and especially that it is not concentrated on one or two walls of the room.
(Walls, as here used, refers also to the floor and ceiling.)
According to this simplification, the time required for the intensity of the sound to be
reduced a specified amount will depend upon (1) the number of reflections which occur
per unit time, and (2) the amount of sound energy which is absorbed at each reflection.
If the room is a large one there will be only a few reflections per second; and in addition,
if but a little sound energy is absorbed at each reflection, it will require a relatively long
time for the intensity of ordinary sound to be reduced to the threshold of audibility.
Such a room will be excessively reverberant. On the other hand, if the room is small and
the boundaries highly absorptive, the room will be free from reverberation. Since the
average intensity of speech or music in a room is of the order of one million times the in-
tensity which is just barely audible, and since the hard, rigid boundaries may reflect as
much as 98 per cent of the incident sound energy, it is apparent that an appreciable time,
amounting to several seconds in many instances, is necessary for the sounds of speech or
music to be reduced to inaudibility.
Thus, consider a room having a mean free path of 51 ft. Since the velocity of sound at
room temperature (20 deg cent) is approximately 1122 ft per sec, there will be in this room
just 22 reflections each second. Hence, if the initial sound in this room has an intensity
of one million threshold units, and if 98 per cent of the initial sound energy is reflected at
each encounter with the boundaries, to reduce the sound energy to one-millionth of its
initial amount would require n successive reflections, where n is given by 0.98n = 0.000001.
Solving, n is 684; that is, it requires 684 successive reflections in this room for the sound
energy to die away to inaudibility. Since 22 reflections occur each second in this room,
the time required for the sound to die away to inaudibility is 684 ~ 22, or 31.1 sec; that
is, the time of reverberation in this room is 31.1 sec. By a similar consideration it can be
shown that if this same room were completely lined with a material that reflects 50 per
REVERBERATION EQUATIONS
12-43
cent of the incident sound energy the total number of reflections would be reduced to 19.9,
and the time of reverberation would be of the order of 0.9 sec. These simple considera-
tions neglect the absorption of sound in the air, which at high frequencies win greatly
modify these calculations. This type of absorption will be considered later in this section,
ine tormulas to which such approximate theories lead are sufficiently valid for most
practical purposes in rooms which are bounded by materials having the same coefficient
of absorption. However, in rooms bounded by materials having widely different coeffi-
cients _of absorption, the formulas approach validity only as the decadent sound in the
room is made to approach a completely diffuse state. It should be clearly recognized
therefore that the formulas which will now be presented must be used with caution and
understanding, especially with reference to the average coefficient of absorption in rooms
which are bounded partly by highly reflective and partly by highly absorptive materials.
19. REVERBERATION EQUATIONS
The early experiments of W. C. Sabine show that the time of reverberation in a room is
proportional directly to the volume of the room and inversely to the total amount of
absorption supplied by the boundaries of the room. Sabine was able to determine exper-
imentally the constant of proportionality k between reverberation time T and the volume
V divided by total absorption a. Thus,
*-?
The value of k as determined experimentally by Sabine for a large number of rooms of
different shapes and sizes, at normal room temperatures, is approximately 0.05 when V
is in cubic feet and a is in sabins (British units) and 0.164 when F is in cubic meters and a
is in square meters (metric units). A few years later, Franklin and also Jaeger obtained
this same equation from theoretical considerations.
This equation was used for nearly 30 years for calculating the reverberation time of
either contemplated or finished rooms. Even the fallacious conclusion to which the equa-
tion leads for a room with totally absorptive surfaces, namely, that T = kV/S instead of
zero (where S is the total surface area of the room), was overlooked or was not sufficiently
disturbing to destroy confidence in its validity, until recently. The equation is satisfac-
tory in practice for frequencies between about 200 and 1000 cycles in the large majority of
rooms in which the absorptive material is distributed and in which the rate of decay of
sound is slow; that is, the equation applies to "live rooms," provided the frequencies are
high enough to be well above the fundamental resonant frequency of the room but not
high enough to involve a consideration of the attenuation in the medium,
MODIFICATION OF THE REVERBERATION FORMULA. A more satisfactory
reverberation formula can be obtained by recognizing that the decay of sound takes place
discontimtously, at time intervals equal to the time required for sound to travel the mean
free path. The mean free path is given for rooms of conventional shape as 4V/ S. Strictly
it is dependent upon the shape of the
room and the location of the source, 'OBO
so that the equation is not accurate
for rooms of peculiar shape. Thus, ^
for the usual location of the source of t -015
sound and for the first 25 successive JJ
reflections, the mean free path is "|
4.3V /S for a large church or cathe- J ~0io
dr al of cruciform shape and is 3.7 V/S g
for a room with large horizontal di- s.
mensions and a low ceiling, the usual g .005
shape for large office and work ^
rooms.
Allowance must also be made for
the absorption of sound in the air of
100
20 40 60 80
Peroet* Retake ycrnfeffi^ at-fiG0 (X
FIG. 1. Coefficients of Absorption of Sound in Air Coxt-
tainine Different Amounts of Water Vapor, for Frequencies
of 1500, 3000, 6000, and 10,000 Cycles
the room, which is of considerable
importance at the higher audible
frequencies and especially in large
rooms. The curves of Fig. 1 give
the absorption coefScient m per foot for plane waves in air at 20 deg cent. It will be seen
from the curves in Fig. 1 that m has a maximum for a certain concentration of water
vapor, different for each frequency.
12-44 ACOUSTICS
Based upon the inclusion of these factors and a mean free path of 4F/3 the time of
reverberation is
(2)
-S)] '
where c is the velocity of sound and 5 is the arithmetic mean of the absorption coefficients
of all the boundaries of the room.
At room temperature, 21 deg cent, c — 1125 ft per sec, so that for most working condi-
tions
T = _ 2^51 _ (3)
AmV - Sbi <l - a) ^'
in British units or
in metric units (see above). For frequencies below about 1000 cycles, m is so small that
the first term in the denominator of eqs. (2), (3), or (4) can be neglected, that is, the ab-
sorption in the air is inappreciable; whereas, at high frequencies (above 5000 cycles),
this term may become larger than the second (or surface absorption) term. At sufficiently
high frequencies (above the audible range), the second term will become negligible, in
which case the rate of decay and consequently the time of reverberation will be independent
of the size of the room.
The foregoing reverberation formula, eq. (2), is sufficiently valid for practical purposes
provided the sound in the room is thoroughly diffuse throughout the decay. This condi-
tion is realized for frequencies above about 250 cycles in all but very small rooms, provided
all the boundaries of, the room have approximately the same absorptivity, or provided
suitable rotating paddles or "warble tones" are used to "mix" the sound in the room.
Suitable precautions, such as those just mentioned, can be taken in making measurements
in an acoustical laboratory, such as a reverberation chamber. In many rooms encountered
in practice, the absorptive material may be concentrated on a single surface, as when a
carpet, upholstered seats, and audience are all located on the floor, and the other surfaces
in the room are highly reflective. In such rooms, especially if the opposite walls are paral-
lel and not too far apart, the decay of sound will not conform to the approximately expo-
nential decay predicted by eq. (2) but will consist, first, of a rapid rate of decay while the
sound is relatively diffuse, and second, of a much slower rate of decay, made up largely
of a horizontal now of sound energy between the parallel and highly reflective walls, i.e.,
of modes of vibration which are directed at grazing incidence to the floor. The time of
reverberation in such a room will be longer than that calculated by means of eq. (2),
using an arithmetical mean for 5.
This is borne out by some oscillograms of the rate of decay obtained in a small room,
8 ft by 8 ft by 9.5 ft (high), with the floor covered with a material having a rated absorp-
tion coefficient of 0.60 at 512 cycles and with the walls and ceiling finished with painted
concrete. The first part of the decay (15 to 17 db) was relatively rapid, 95 to 100 db per
sec. This was followed by a much slower decay, 38 to 40 db per sec. If the first part of
the decay is used for calculating the time of reverberation T and the absorptivity of the
floor material or, we obtain T = 0.61 sec and a = 0.55. If the latter part is used, T « 1.54
sec and a. = 0.22. It will be noted that the first part of the decay, while the sound is
relatively diffuse, yields a value for a which agrees fairly well with the rated value of 0.60
and therefore conforms reasonably well with the requirements of eq. (2), whereas the
latter part of the decay, which is made up largely of the horizontal modes of vibration,
is much slower than would be predicted by eq. (2). This is an extreme example of the
inadequacy of eq. (2)-, which is based on geometric acoustics, to account for the true nature
of the decay of sound in a room in which the absorptive material is concentrated on one
wall (or floor or ceiling). Wave acoustics, on the other hand, accounts for the observed
results very satisfactorily.
Fortunately, for the best acoustical quality in a room the absorptive material should be
distributed on all surfaces of a room so that the rate of decay will be at least approximately
the same in all directions, and under these circumstances eq. (2) will yield results which,
as a rule, do not differ more than 10 per cent from the observed values. Furthermore, in
very large rooms, as in theaters, school auditoriums, and churches, there is very little
tendency for the reverberation to persist in two dimensions, even though most, of the
absorption is concentrated on the floor or on the floor and in the ceiling, (1) because the
dimensions of the room are large compared with the wavelengths of the sound, and (2)
beeaiase* the 'architectural treatment of large rooms usually involves structural forms and
ornamentations which tend to diffuse the sound during free decay.
ROOM RESONANCE 12-45
In such rooms, provided there are no curved surfaces giving rise to concentrations of
sound, the nrst SO db (or more) of decay conforms very closely to eq. (2); and it is this
portion of the decay that is pertinent to the acoustic quality of speech and music in
rooms. Stated otherwise, the rate of decay after the first 30 db of decay is of little conse-
quence, since in articulated speech or music such residual sounds will be so weak as to be
completely masked by the primary (and much louder) sounds that follow. It is apparent,
therefore, that eq. (2) is satisfactorily valid for the practical calculations of reverberations
in most rooms. In many small rooms, such as are frequently used for radio broadcasting
or for the recording of sound, it is important that the sound-absorptive materials be dis-
tributed quite uniformly throughout the room if eq. (2) is to be applicable. The true rate
of decay of sound in small rooms is greatly dependent upon room resonance.
20. ROOM RESONANCE
A room is a resonant chamber, with resonant properties similar to those of a violin
string, an organ pipe, or a diaphragm of a telephone receiver, except that in general the
resonant properties of the room are much more complicated than those of one- or two-
dimensional systems. Thus, if the dimensions of a rectangular room are Ii, Zj, and Zj, tbe
"resonant" or normal frequencies v for the room are given approximately by
- c \ If If
" = 2U? + ^ +
where c is the velocity of sound in the room, and wj, ns, and n* are order numbers having
values of Or 1, 2, 3, In a room where li - 8 ft, It = 8 ft, and Z* = 9.5 ft, the gravest
mode of vibration is given by n± =* nj = 0 and ns = 1 ; that is, the room resonates as does
an organ pipe, 9.5 ft long and stopped at both ends, when vibrating at its gravest mode.
The wavelength of this gravest normal mode is 19 ft, and tbe frecpieaey (assuming c =
1125 ft per sec) is 59.2 cycles. Other resonant or normal frequencies, in ascending order,
for this room, are 70.3, 92.8, 90.8, 116.0, 119.2 cycles, and continuing in a triply iofinite
series" of frequencies corresponding to increasing values of the »*s. When none of the n's
is zero the resonant standing waves are oblique, and when one or two of the n's are aero
the waves are tangential; that isr the waves move parallel and gracing to one or two, re-
spectively, pairs of walls in the rectangular room.
The above-enumerated normal frequencies for the room under discussion have been
observed, both by the "reinforcement" the room gives to steady tones of these frequencies,
and by the transient decay of tones which have approximately these frequencies. Thus,
Fig. 2 is a series of oscillograms showing the free decay of sound for this room when it is
excited with tones having different "driving" frequencies between 90 and 101 cycles, as
indicated above each oscillogram. When the room is excited with a frequency of 92.9
cycles, which corresponds closely to the normal mode having a frequency of 92.8 cycles,
the free decay is made up almost exclusively of this one mode, and its decay rate is* smooth
and almost exactly exponential. Similarly, when the room is excited by any other fre-
quency which differs only slightly from 92.8 cycles, the free decay is made up of this one
mode, and the frequency during decay is not the <$rm«g frequency but is always ike fre-
quffncy of this normal mode. When the room is excited with a frequency of 96.7 cycles,
•vrhich is about midway between the frequencies of the two modes of 92J3 and 99.& cycles,
the free decay is made up of these two normal modes, which are about equally excited,
giving rise to the pronounced beats of about 7 per second, as expected, since the two natural
frequencies differ by 7 cycles. When this same room was excited at a frequency of 118
cycles, the oscillogram of the free decay revealed the coexistence of beats at about 3.3
and 19.3 cycles, which no doubt arose from the simultaneous excitation of the tliree neigh-
boring normal frequencies of 99.8, 116.0, and 119.2 cycles. No matter what frequency is
used for exciting the room, the "reverberation" always consists of the free decay of ose
Of more of the room's normal modes of vibration.
The foregoing tesults demonstrate that reverberation is not the persistence ol rays of
sound which continue* after the source is stopped, as rays of sound successively rejected
back and forth in the room, but rather is the free decay of one or more (and usually many)
modes of vibration. However, Strutt has shown that the forma! law governing the free,
damped vibration of the sound in a room approaches asymtotically the simple reverbera-
tion law of eq. (2) as the wavelength of the exciting sound becomes short ia comparison
with the wavelength of the gravest mode of vibration for the room. Thus, in a room
(assuming the ab&orpifcive material to be fairly well distributed) having its longest dimen-
sion 10 f t» which is about the smallest loom in widen acoustics is a factor of hnportaee,
12-46
ACOUSTICS
the wavelength of the gravest mode is 20 ft. In such a room, sound having a wavelength
of one-tenth of that of the fundamental, namely, 2.0 ft, would be sufficiently short to
conform reasonably well to eq. (2) . , ^ T_ .L .T.
In other words, when the room is filled with sound having a wavelength shorter than
2.0 ft, that is, a frequency greater than about 560 cycles, the modes of vibration which
are excited are so numerous and their frequencies so close together that the sound in the
room is essentially diffuse and, therefore, the requirements are fulfilled for the approximate
theories of reverberation described in the earlier paragraphs of this section, especially if
FIG. 2. Oscillograms of the Decay of Sound in a Small Rectangular Room, Showing that the"Decay
of Sound Consists of the Damped Free or Normal Vibrations of the Room
the absorptive material is distributed uniformly over the boundaries of the room or if
some means are provided for mixing or diffusing the sound during the decay. In large
rooms, such as concert halls, church or school auditoriums, and theaters, the lowest modes
of vibration are usually in the subaudible range of frequencies, so that the elementary
theory of reverberation applies with adequate rigor in such rooms for all frequencies above
about 100 cycles, and the effects of room resonance usually can be neglected. (For further
details consult M.J.O. Strutt, Zeitschrift angew. Math. Mech.; Knudsen, /. Acous. Soc.
Am., Vol. 4, 20-37 [1932] * and Morse and Bolt, loc. c#.)
REVERBERATION IN COUPLED SPACES. When two or more inclosures are
coupled by means of openings such as open doors, passageways, or even thin partitions
which are capable of transmitting an appreciable amount of sound, the reverberation in
each inclosure is affected by the reverberatory properties of the other inclosure. Thus,
most au-ditoriums of the theater type are divided into at least three coupled spaces — the
stage, the main portion of the auditorium, and the space under the balcony. Even a
REVERBERATION AT DIFFERENT FREQUENCIES 12-47
long sound-recording studio, one end of which is reverberant and the other end non-
reverberant, may be regarded as two coupled spaces. Office space is often divided into a
number of coupled spaces; and a great complexity of coupled spaces often will be found
in cathedrals, consisting of nave, transepts, choir, sanctuary, aisles, chapels, balconies,
and organ chamber. If the mean free path can be determined for such coupled spaces, and
if all surfaces have approximately the same absorption coefficients, the regular reverbera-
tion formula, using the appropriate value of k, will give the time of reverberation for the
entire room. (See Knudsen, Architectural Acoustics, Chapter V.) But it is not always
feasible to determine the mean free path for a complicated combination of coupled spaces,
and it is very improbable that all surfaces will have even approximately the same coeffi-
cients of absorption. In many instances, therefore, it becomes necessary to consider the
reverberation in each of the several coupled spaces, and to adjust the reverberation time
in each space to the optimal condition.
Many rooms have poor acoustics because of failure to recognize the effect of coupled?
spaces. Thus, in many school auditoriums containing a balcony, it is common practice-
to install nearly all the absorptive material hi the ceiling. In some auditoriums the walls
under the balcony, the soffit of the balcony, and the floor under the balcony may be of"
hard, reflective materials, as hard plaster and concrete. If, in addition, the seats under
the balcony are of the unupholstered type, the space under the balcony will be very re-
verberant although the space in the main part of the auditorium may be quite free from
reverberation. During the growth or decay of sound in such an auditorium there is a
transfer of energy between the two coupled spaces, with different rates of growth or decay
in the two spaces. During the steady state the rate of transfer of sound from the dead
space to the live one is equal to the rate of transfer in the opposite direction, During the
very early stages of the decay these rates of transfer are nearly equal, but since the sound
decays' much more rapidly in the main part of the auditorium than it does under the-
balcony, there soon will be established an excess rate of flow from the live to the dead
space, and the result is that the reverberation is prolonged in the main part of the audito-
rium as well as in the space under the balcony.
In order to overcome this undesirable condition it is necessary that the rates of decay
in both spaces be nearly equal (or that the rate of decay in the smaller space under the
balcony be greater than the rate of decay in the main part of the auditorium). This in-
volves a determination of the reverberation in both spaces, which in turn necessitates the
assignment of coefficients of absorption to the opening which couples the two spaces. It
is not possible to assign precise coefficients to these openings. The coefficients will depend,
in general, upon the size and shape of the opening, the depth under the balcony, and the
amoxmts of absorption under the balcony and in the main part of the auditorium. But if
botli spaces have approximately the same rates of growth', as they should for good acous-
tics, the "effective coefficients" will be of the order of 0.40 to O.SO — nearer the lower limit
for shallow recesses which contain a relatively small amount of absorption. Similar con-
siderations apply to the stage opening which couples the stage and the main part of the
auditorium.
Many theaters, churches, memorial halls, and other auditoriums are often coupled, by
means of door openings or archways, to rooms or corridors which are excessively rever-
berant- In such auditoriums, even though the reverberation in the audience space has
been adjusted to the proper value, there will be a "feedback" of reverberation from the
adjacent reverberant rooms into the main auditorium. Thus, auditors in a theater who
a,re seated near an opening to a reverberant corridor, foyer, or anteroom will be disturbed
by the excessive reverberation in the adjacent room. It is advisable in all such cases
either to close the openings or to use an adequate amount of absorption in all spaces which
are coupled to the audience room. In general, such anterooms, foyers, or corridors, unless
they are used for speech or music rooms, should be as non-reverberant as possible.
21. REVERBERATION AT DIFFERENT FREQUENCIES
Unless otherwise specified, it is generally understood that the time of reverberation refers
to a pure tone of 512 cycles. Although the calculation of reverberation at a single fre-
quency, as 512 cycles, will suffice to represent the reverberation in a room at other fre-
quencies provided the absorptive material in the room has nearly the same absorptivity
at all frequencies, or provided the variation in absorptivity is known, it is obvious that
such is not the case if the absorptive material has widely different and undetermined ab-
sorptivities at different frequencies. Thus, an acoutical plaster, 1/4 in. thick, applied to-
concrete or tile, may have coefficients of absorption of 0.06 at 128 cycles, 0.36 at 512 cycles,.
/vnd 0.72 at 2048 cycles. If such plaster is applied to the entire inner surface of a room
12-48 ACOUSTICS
the reverberation time at 128 cycles would be at least six times as long as the reverbera-
tion time at 512 cycles, and the time at 2048 cycles would be less than one-half of the 512-
cycle time. If the reverberation time in such a room is 1.25 sec at $12 cycles, it will be
at least 7.5 sec at 128 cycles. To describe this room as one having a time of reverberation
of 1.25 sec — which is regarded as close to the optimal time for good acoustics — certainly
does not describe the reverberatory properties of the room ; and such a room will be highly
unsatisfactory. There will be complaints of excessive reverberation, and the room will be
too reverberant for the bass notes of music, and even the low-frequency components of
speech will be reverberant and overemphasized. On the other hand, the higher tones and
harmonics in music will be suppressed owing to over-absorption at the high frequencies.
Such rooms are particularly objectionable for recording or broadcasting purposes.
It is necessary therefore to specify and calculate the reverberation times for representa-
tive frequencies throughout the entire range used in speech and music. It will be found,
however, that, if calculations are made at 128, 512, and 2048 cycles, the resulting times
will give a satisfactory description of the reverberatory properties of the room. In
recording and broadcasting studios it is desirable to consider frequencies as high as 8000
cycles.
In general, the reverberation time at 128 cycles should be slightly longer than the time
at 512, and the reverberation time above 512 should remain nearly constant. (See Fig. 10,
p. 12-75, for present recommended practice.) The success or failure in the acoustical de-
sign of rooms will depend upon the selection of absorptive materials which will give the
pro-per reverberatory characteristic throughout the entire range of frequencies used in
,-speech and music.
22. THE MEASUREMENT OF REVERBERATION AND ABSORPTION
COEFFICIENTS
The reverberation time of a room, or the total absorption of the room, for rooms in
which geometric acoustics will apply, can be determined by measuring either the rate of
decay of sound or the time for the decay between known intensity limits. For determining-
the sound-absorptive coefficients of materials it is customary to make measurements ol the
rate of decay of the sound in a reverberant room first when the room contains a certain
area of the acoustical material to be tested and again when the material is removed from
the room. In order to approximate conditions which wiEf justify the applicability of
formulas based on geometric acoustics, it is better to distribute the absorptive material
on three (non-parallel) walls rather than concentrate in one area on one walL By means
of eq. (3), the value of 5, and consequently the total absorpjfckxn aS, can be calculated.
The absorption of the acoustical material in the room is assuanaed to be equal to the dif-
ference between the absorption of the room witli the material m it and the absorption of
the room with the material removed. This is equivalent to assuming that <x is the arith-
metical mean of all absorptive surfaces in the room, an assumption which is; justifiable1
provided the sound in the room is kept thoroughly diffuse duEriag the steady state and
the decay. Warble tones at least 100 cycles in breadth with a. warble frequency of at
least 4 or 5 per sec should be used for test tones below about 500 cycles, and, unless the
room be bounded by diffuse reflectors, large rotating vanes shGHzkf be used for test tones
of all frequencies. The test tones should be pure.
When these precautions are taken the rate of decay will confem satisfactorily to the
theoretical rate, and, if the test area is as large as. about 72 sq ft im a room having- a volume
about 5000 to 10,000 cu ft, the difference between the rates of decay with and without the
acoustical material in the room will be large enough to yield coefficients of absorption
accurate to about =fcO.G5 for frequencies up to 2000 cycles. At higher frequencies the
absorption in the air, which may change during: the time required for the completion o£'
the test, is so large a factor that errors of the order of dbO.10 azee isnavoidable unless the
reverberation room is carefully air-conditioned. Even with am air-conditioned room the-
accuraey is not satisfactory at frequencies above 4000 cycles, because the absoarptioru ib
the air is such a large factor that the difference between the rates of decay with and with-
out the acoustical material in the room is not appreciable nnTea& the test area JB greatly
increased.
The rate of decay is measured by some type of reverberating naeter which m general
coaasists. of (1) a suitable source of steady or warble tones, usually a vacuum-tube oscillator,,
an electrical low-pass filter, a power amplifier, and an eleetrodymamic laudspeafce^;, (2) a,
iMgh-quaEty DMcrophone and amplifier; (3) an electrical attenuate for varying the e^fa*
oC ibe ampfifier; and (4> either a recorder which registers comtBiuaasly, on a moving, pape^-
MEASUREMENT OF REVERBERATION AND ABSORPTION 12-49
chart or on a light-sensitive medium, a graphic record of the decay, or some type of indi-
cator, usually a relay and chronograph, by means of which the rate o£ decay can be de-
termined.
The Bell Telephone Laboratories, Inc., among others, have developed a high-speed level
recorder which gives a response proportional to the logarithm of the actuating current, and
the instrument is so adjusted that the record gives directly, when the paper tape is moving
with constant speed, the rate of decay of the sound in decibels per second. If the decay
follows the exponential law, the curves will be straight lines. However, since the decay
consists of several contiguous frequencies (normal modes of vibration) in close proximity
to the frequency of the exciting tone, there wiH be interference between these several
frequencies (each of which decays exponentially) so that the resultant decay curx-e gen-
erally will be quite irregular. Typical decay curves obtained with this instrument in the
reverberation room of the Bell Telephone Laboratories are reproduced in Fig. 3. As these
<Tinje In Seconds
\
>
/ \
^v /
\
/ ^
%I /
. V
/ V
4 i — i " & — T
Time in Seconds
FIG. 3. Decay Curves Obtained with Bell Laboratories High-epeed Level Recorder
records show, the decay is not strictly exponential but, except for minor fluctuations which
can be attributed to the resonant or interfering phenomena discussed in article 20, the
general trend of the decay conforms very satisfactorily to the exponential law, over a
range of 40 db; and, if a straight line is fitted to the recorded curve of decay, the slope of
this line will give the rate of decay with sufficient accuracy for practical purposes.
The curves labeled 9, 10, and 11 were made with a pure tone and a single microphone
and with the recorder adjusted to "follow" maximal speeds of decay of 240, 120, and 60
db per sec, respectively. In 9, for example, the recorder is capable of following the actual
decay much more closely than it is in 11, where only the slower variations of decay are
recorded. The curves labeled 12, 13, and 14 were made at the same recorder speeds, re-
spectively, but a warble tone was used instead of a single pure tone. The advantage of
the warble tone for reverberation measurements is obvious from these decay curves.
In the chronographic type of reverberation meter, in use in many laboratories. It is
customary to measure the tune for a given drop in level, increasing the drop in steps of
5 or 10 db. A good meter of this type is the one developed by F. V. Hunt (/. Acows. Soc,
Am., Vol. 5, 127 [1933], and Vol. 8, 34 [1936]), which is almost automatic. As usual, the
sound source is a warble tone oscillator. Several microphone positions throsighiOiit t^e
room are used to insure a good average, and the reverberant sound thus detected and
amplified is rectified, and rapid fluctuations are filtered out. An automatic timer tunas
off the source, always at the same phase of the sound wave, when the soimd level ia tiae
room has reached a predetermined level, indicating the time for this decay. This is
repeated 40 or more times, and the average value is used for plotting the <$ecay earv^
Figure 4 is a composite curve obtained by Hunt, showing the average decay for a warble
tone of 1000 ± 200 cycles throughout a course of 80 db. By comparing the observed
decay curve with the dashed straight line, it will be seen that the decay is satisfactorily
exponential during the first 50 db of decay, the portion of the curve which should be tatsed
in making sound-absorption measurements. The non-linear decay from 50 to 80 dfe
probably results from the more slowly damped tangential modes of vibration, which pre-
dominate during the latter stages of the decay*
12-50
ACOUSTICS
A third method of measuring the decay rate is the oscillographic, illustrated in Fig. 2,
which gives a detailed picture of the frequencies, as well as the intensity, throughout the
course of the reverberation. .
Reverberation measurements are useful not only for determining the coefficients of
sound absorption of acoustical materials in a reverberation chamber but equally for deter-
mining the reverberatory proper-
ties of all rooms. In general, a
reverberation meter should be
capable of making measurements
at all frequencies between about
128 and 4096 cycles and should
reveal the detailed nature of the
decay of the sound, especially
during the first 30 to 40 db of the
decay. In music rooms, record-
ing or broadcasting rooms, and
theaters, it is desirable to make
measurements at frequencies as
high as 8000 cycles.
For additional methods for
70
60
50
DB
30
10
N
Bar
Fou
S^ Slope o
Composite
e Room
r Microphom
F Straight Po
from Linear
Decay Curve
1000 ±200
> Positions
rtion— 23.6
ty 0.006
cps
DB Sec
~^T*Ave Dev
N
\
\
V
FIG. 4.
measuring reverberation and ab-
sorption, consult Knudsen, Archi-
tectural Acoustics, Chapter VII;
Sabine, Acoustics and Architec-
ture, Chapter VI; Olson and
Massa, Applied Acoustics, Chap-
Decay Curve, Based on Measurements of Average ter XII; and Beranek, Acoustic
Time for a Given Drop in Level. (Hunt.) Measurements.
1
2 3
Time - Seconds
23. COEFFICIENTS OF SOUND ABSORPTION
In the following charts and tables there is given a fairly complete listing of the coeffi-
cients of sound absorption of the materials which are used in building construction, espe-
cially for acoustical purposes. Many of the same materials have been measured by dif-
ferent investigators, and the results are not always in good agreement. Such factors as
actual differences in the samples, differences in the methods of measurement, differences
in the size, shape, and location of the samples compared with the size and shape of the
test rooms, the purity of the test tone used, and errors inherent in the use of reverberation
methods and formulas based on geometric acoustics when wave and not geometric acous-
tics applies are probably responsible for this lack of agreement. Where large discrepancies
have existed, certain liberties, guided by experience and the probable influence of wave
acoustics, have been taken in averaging results.
Most of the materials manufactured by the leading acoustical concerns in the United
States have been tested in the same laboratory by the same method; this facilitates com-
parison of different materials. The authority for these measurements is the Acoustical
Manufacturers' Association; the tests were made at the Riverbank Laboratories. The
authorities for the other measurements are listed in Table 1.
Much progress has been made in the development of acoustical materials during the
past decade, and this progress will continue. Many improved and new materials will be
described in subsequent issues of the Bulletin of the Acoustical Materials Association, which
is published at frequent intervals. (These bulletins should be consulted; they can be
obtained from the Acoustical Materials Association, 205 W. Monroe St., Chicago, Illinois.)
Table 1, on sound-absorption coefficients, includes considerable data concerning acousti-
cal materials in addition to the coefficients of sound absorption, such as the type of the
material, the nature of the mounting, the light reflection coefficient (usually as painted by
the manufacturer), the weight per square foot of the material, and the unit size of the
material. The numbers used to describe the types and mountings are those used by the
Acoustical Materials Association. The legend for these numbers is given hi the table.
In choosing materials for noise-reduction purposes, in offices, factories, restaurants,
hospitals, etc., it is customary to rate the materials acoustically in terms of the arithmetic
mean of the^ coefficient at 256, 512, 1024, and 2048 cycles. This average value is called the
ywise-reduction factor. It is better practice, however, to choose materials that have the
absorption characteristics best adapted to the characteristics of the noise to be absorbed
It is especially important to avoid materials having very low absorption at the low fre-
quencies for sounds which are made up predominently of low frequencies.
COEFFICIENTS OF SOUND ABSORPTION
12-51
e
3
-*r °V 1
2
*.
J
i
1
^^^----^^^^^^^^^^2!^ S
xxxxxxxx* xx3* xxxxxx-i
r
o-
«*>rr>-«-^r«O «*»-^- OC9 «nfV
*
1
<*>«r*< O ^ — — o — — ^ — O O — — O
1
-j.2
e3 oi
i.£
•ai
?«
-1
'fR
ooaonteoooeoaoco <*•* ^ ^ rsjoj-^r-^-
0 S
•S"S
s^
a1
S 0
56
c=>
nil
^ <
I.t
~^«M^,, ,,«« ^^^^^^^
1S-S1 |
>O
^(OO^^-OOO ^cocv NO 0^
J.Q § j> j> j,
?
o -
312! ! !
oo
•fl-
O
*— t>. - — ^r<c3oor4 oooo-«* coo»o^^^«^r«»oo
•siSi § ~
«M
0
" § * 0 « . 1
JO 0° *JCT-t^j S TS • O
(C
^
S
^.ovovtx — -«-tn«> o^-rx. r^Noratno '.
« -foil -gl S *
•§ 1 3 S 3 i S -2 c
c
S
"3
O
£
o :
1 &1*5 If § .-
*§
rs,
,S
a mi is m*
NM' «pf_,**-«jj en o *C
0
^
en
•t^
o • • • • •
d c: o £ =3 ;" § uca
o '§^,5 §g |^r
S
(B
O
0
S^S^^^SS SJQS ^^^5:^^ :
& ails. *f |^|
?
CD
S -2 I 1 5 ^ 1 § -S "S
>
1 111- .-sT |gu
SS <M— SSf^ — <N|<=) CN« —
1 |l£-88^l si*
s
0
1 i«tiil§ -S 1^
g §^ g o S o.P' S > o
w ^ill!|!-2|
t ««3"3i>,3«'£ 5<si«
A |.IIl^|1l^l
a S!J!M5!*S
ii
fcC
a
I
?
oustlcal Units— r
If
— rs ^ - <N — r* c< m — M M^— M-^M
."§!§
1C XI
Illllfllsl
ISlssN 131
i
e>
2,
^
sg>>»» >^^ ss>>>> ;
aa-a's-ai^ g-aS
OO&DPOS oz<;
j<
S'r
..,.<-, »_ o «« -
«K>>^ag -««
p
fl "
__«ee__e «M o o e - o o - - o
Kb
3 -1
H o
s s
*o *o
3 IH
S
||| j
. . . J. » -r •<• ... ...,,..
: : 8866 : *: :::::::
Material
oc S.2.1.1 ::: ::••••:
§§ ^^-2^as "Sfefe ..••••-
llllllil III lillill
JJsslsl! 1|| |||||ll
12-52
ACOUSTICS
e
i
*s
3
|xxxxxxxxxx||||-d|||x xx x x x^x^ x x
£
" a1
:OQ
ONeNts»r>,^c3rNi'«><«'b<. •*i-i5)g+i -M ! .' ! i o OOO
&
£
i-
-p
:SSSS : : :S£z: : : : : : : : SK K K S S : :
<-
-3 "
NO
rNi^^0cs»^rooors,ocsoo ON Nooo'.-t^ ^- ^r NO c-i .g c^ co
i
o :
CO
"9-
$££££££££^S £ 3S3££ SS g E S R g S
°
o
£
•*t"
rs
^3
4>
SSS^SNSSSKSS:^ S ^SS^ie 5:2 5 S^ o^ § § £
-s
—
-2
o
&
o
PS
4>
5
S£££K3E££££S § S$3S£ ££ § S 5; R SN 5
O
rT
0
NO
«A
i
ooorj.oD-r^^cjjscs^NO - jr NO - jq o cc o - - - o o^ rx
cs
*3
0
to
CNJ
— o a o — o o — 2 JQ 2 Z! J?J i£ es, „ 2 — cQ — — So— — CM
EH
0
j
j
"i
<
V
<
f
5
a
3
?
oustical Units — r
..^-..-^-^ „ NM_M_ _ _ „ _ „ „ „
I
I
>a
•f
<
i^^iiigrs i IIIIH £> > > " " - ~
|s
-<»-e»orN1i>.oo — o IA-^--^ CNI ONON
'«r»nir%GOco»rv«AC?OOaoin O l>.u->"»-^-O *f\ \O O O O O »— J—
ooooo oo — — — oo — o* o' o" o* — PS o' — — — — *J rs'
t.
jlllliilll^ 5 ,0 i „ . . II
SSSSfS&gBJJJJ | 3^6 | 1 1 In- *. II
Illll222i!|| J |||l III |1 1| ^ 1
§^<<<^^^^||s S ll^o ll^l^l^ ^ |
* - - -J2 pg " " I *.j>4 ". aT o" of
**
•S _•_•,*„• : : : : : ^©l® :|| :.! | J J 1
1
^ . . , -ao:o: : : :Ss§-S :|H :3 § § 3 3
0jCJ«ja5«.S.5.Soo;o"So*S .vS-.-o o cs g o
I "fill
COEFFICIENTS OF SOUND ABSORPTION
12-53
i i
: : : : :
I
0 0
0 0
c* m a,
fO
:
o^cst^r^^o^ r, o,
(S CS O
- m oo oo oo Jn ™
c<\ — — r*-»*o to r* +o *o e»
*n oo GO t%, eo oo oo «n co o-
o
0
s ¥ $
•*•
S^ S S £ $£
^^^ors.^-o.-ojn g ^
0
0
O CM TO
m in t*\
-m O — oo bxo
. \o o* oo oo «n r>>
,3
£K£S£££§£S£ S S
0
*
0
0
PR
*i
0
s £ s
tx, <T| OO OO vO vO
B
«n CN — o o — ONOO — <s «n r> -«•
o
j
0
oo oo r->
cc
-^dro o <H ^r <N o»
5
i-4-9-m^*<-\<'*-ir»wior<'l\o »A ««
o
^
0
Is .° .S "^ ""S
F-J o o •-; --j
S
1
0
•g ^ ,0 o "g
£3 70 g g
Q02 JC O O
J^
!
a
5=5
si o
t—
• ;
e g
-§s
fflS
^0
*~ ^*
• S 1C 5
e
V
mo »n o »n ^ o
00000000000 O O
l"4
-a-^.^S
•s e *5
Val-Porter Co,,
Los Angeles
Val-Porter Co.,
Los Angeles
"d oS "§ =4
S S S S g
|||||||||°
OO jEjojnajns ** C
^ £ JO ,£t .fl jfi jO ,C -^ -^
Ino,, Chicago, III.
id brown ooats on m
blanket nailed to 1
ing, 20 gage, 0.0764]
nket on floor.
tji ^
}
1 1 1 1
I 1 1 I
ft'S' ft-g-A-g ft-g1 J
«S^_;_:^:^:-: -g *©
||§§g§|| | :.|
jgjfefe^fep? | :|
ican Acoustics,
hard scratch at
icing, Fiberglas
rated metal fac
in covered, bla
» 1 1
1 1 J
^ •< <
5
:i
> -
'jO
v2- &s2- S<2- S«S o:3
^ ^ P^S ^ o e
^ 53J8llJ35§l :l
S'M*hE-5s'3'a'StM gjS ^n3J4^^
5jt.^V,«-(^g^^t>|iPi45;^p«^
•^^^^^^5^^^2'cto § §
S *s«S<2 s
Illll
12-54
ACOUSTICS
o
3
3
<J
>0
o, * r*««s«
?
0
:
00
o
<Mn^^MOOo™
0 »A -f — t^. rx <r» — *> SO !>, 00 0 "*• O tx fS 0
es
0
0
<N
0 — — OOOtN
' -^5 j®52 — zs<s^ S i i^£\ "
.2
d
"~
0
1
s
N
vno — — — — 'O^OIA
o — — — — — oo«s
J
mtn-^-eo — i>.ooo0*AONU^minc«"» * "ooooo
rsi— rsjcstsr^ooof — ffsvno o O®<S(M»A
o
0
S
0 vr>^
CS IN
|
«
CO
or* — — — — — — c<*
o
. ,o — o — ooom»— — ft • — — .
1
o
1
OO
1
o
43
•*-•»- H- 4-
-(-•i- -1- -K
S o o — o — o o o o o o — o oo — m
0
S
0
i
1
O • -IT -*• *«• •*• • •
t>
P
Set Materials for
f\ • O
o I .' !
Hangings, Floor Co
:::::::&
j «• : : : -: : £
.31 : 3 Is
oo OD • P* o*5
II 1 1 ll
• "* A • . . . -^ . . . .
c
.£
fg? * 1 ojl
: : : : : : : :| ° | :^ : :| : : : :
_c
|
<
-« .2 5 * •> °
gj •*» «* £ <H 2< ^ £4
'•1 '• '••'• il&fj i I ! ':
st plaster, applied to burlap,
st Btone, similar to above, ex
otex, papered with crepe pai
otex, as above, with one ooa
isonite, papered with crepe p
isonite, as above, with one oc
neered flats, papered with ore
neered flats, as above, and lit
aolite, ** brushed over burlaj
lj||j||i|i-fj f j |
opQQ^ogcQ>o<D*~oi3®fl« p
-^c»i-?"O'^_v^--Mfcr^d^CtH ®
^ eS c3 -j d ^,=8 3 — -g 3 * O *oS^O<
_C fi S (3 ^ ^ "^ -g .g ^ ^3 ^ _ -^.^.^O^'S S"
OOOO^£>>e§
oddddoddoooQQ^ocDooSl
COEFFICIENTS OF SOUND ABSORPTION
12-55
Hard Plasters, Masonry, Wood, and Other Standard Building Materials
™m^mm™m
— — *— «
-™— _
** Small granules of exfoliated verinioulite bonded with a planlio, tacky binder,
ft These coefficients aro estimates mado by the compiler.
Authority: (1) Bureau of Standards, (2) Acoufltioal Materials Aasuuwuou, (3) V. O. Knudaen, (4) P. E. Sabine, (5) W, C. Sabino, (0) Building Research Station, (7)
F. R. Watson, (8) Wente and Bedell, (9) average.
r>. cs
0 0 .
o
; :
0 O 0 0 0 0 —
t
m «N (N
O 0 0
•i— 4-
4-4-
0 0
ooo^^^o—
— eo
<•* so r>i *n *r» co -o *A
o NO oo -o ^o t*.
o
xr^ ! I :<n^oors™_«
oco <n£ cnr^ro "
o ...
•w m — o en
men -
O 0 O
0 0
„•
0
ther Objects
00 •
0 O 0 O 00 —
o*
*n IN. -«• «— —
cn-r I
0 ...
O
•§
Oj
S
"3
o
s
t
O O 0
4-4-
. . - oO
0
— — «— — C* 0 —
0 0
OO OO
. . u-> . . - va >a-
'.•&
ice, Individual Pers<
^ ' ' °° 1
§
ts on metal lath, on woo
1
uds, 1 6 in. o.c
1
Audience, mixed, seated in theater chairs, single padding on b
Audience, mixed, seated in church pews
Chair, American logo, full upholstered in mohair
Chair, box spring, pantasote seat and back, plywood on rear; a
Chair, plywood seat, plywood back; seats up ,
Chair, spring edge mohair seat and back, plywood panel on rea
ir covered seat and back
"S - • • -
Brick wall, unpainted. .
GlflAS
Interior stucco, smooth finish, on tile. .
MnrKlA
Plaster, gypsum, on hollow tile
Plaster, gypsum, scratch and brown coa
Plaster, lime, sand finish, on metal lath
Poured concrete, unpainted
Poured concrete, painted and varnishec
Water, as in swimming pool
Wood sheathing, pine
Wood veneer, on 2 in. by 3 in. wood st
Chair, like above, with thick, complete!:
Chair, theater, heavily upholatered. . . .
TWorm «/JllH.
seated in American ioge
high school
junior high school
grammar school , .
in, without coat, seated. .
in, with coat, aeated. . , . .
) O O O O O O C
12-56
ACOUSTICS
The table contains absorption data on a number of mineral wool blankets made up of
wool of different densities, and of thicknesses varying from 1 to 3 in. It will be seen that
by suitable choice of density and thickness it is possible to obtain a wide variety of absorp-
tion characteristics.
1.00
,90
x^
^X
J /
^^^^*T
.80
/
f//
/
/
§ JU
*0
•///
/
/
/
3= .60
§ ,
A
CVJ
/
/
.50
c
o
:p /»n
r<^).
/4/3
/
/
1-1"H
2-2"
air Felt
« M
g. .40
J*~
on
^ X
YZ
)/1
3-3"
4-4"
5r //
i n
>"^
A
•5
6-6"
i «
.20
Tfi
_^— -'
\^
,,
3
0 6
0 U
.5 2
50 5(
)0 10
00 20
00 40C
Frequency— Cycles per Second
PIG. 5. Absorption of Different Thicknesses of Hair Felt. (Wente and Bedell.)
In Fig. 5 are shown the results of sound-absorption measurements of Wente and Bedell
on hair felt of different thicknesses. The principal effect of increasing the thickness of a
porous material is to increase the absorption at the low frequencies.
In Pig. 6 are shown the results of measurements at 512 cycles on different thicknesses
of hair felt obtained in four different laboratories. These results show not only the effect
of thickness but also the order of agreement of measurements made at different laboratories.
The manner of mounting acoustical materials influences their absorptivity. Most
fibrous and porous materials increase in absorptivity, especially at frequencies below 500
cycles, as the thickness of the air space behind the material increases. Thus, fiber board
l.UU
g.SO
CM
S.60
c
V
i
o.40
i
5=
&
o
5-20
<,
- — •
-S^
X^-"
/
f
Wf
I. Sabine
.Wente
Paris
. Knudsen
P T
/
/
) 1.0 2.0 3.0 4.0 5.0 6*<
Thickness of Hairfelt-foches
Fi<3. 6, Absorption of Hair Felt as Determined in Different Laboratories
and tiles, acoustical plaster, and similar materials, are more absorptive at low frequencies
when furred out from a dense, rigid wall than when applied directly to the wall.
The absorp*ivities of such materials as acoustical plaster are dependent upon the
composition- as well as upon the manner of applying and drying. If too much binder
material is used the plaster is not sufficiently porous; if an insufficient amount of binder
NOISE MEASUREMENTS 12-67
is used the plaster does not set hard. Likewise, if the undercoats of plaster are too wet
(or "green"), the binder material forms an impenetrable film at the surface, whereas if
the undercoats are too dry the binder material is absorbed by the undercoats, and the
plaster will crumble. In order to obtain good results with acoustical plaster it must be
applied by competent plasterers in strict conformity with the specifications of responsible
manufacturers .
The absorptivity of acoustical plaster or fiber board may be ruined by decoration with
oil or water paint, varnish, distemper, or other materials which will close the surface pores.
Viscous or heavy paints which bridge over or dose the surface pores must be avoided.
Such materials as thin aniline dyes, gasoline or kerosene stains, thin lacquer sprays, or
dry paint dusted on with a pounce bag are satisfactory means of decoration without im-
pairing the absorptive properties of plaster or fiber board. Certain commercial materials
containing large holes, or materials covered with a perforated facing, may be decorated with
lead or oil or any other kind of paint, provided the paint does not bridge over the holes.
In order to facilitate convenient use of the table the materials have been grouped as
follows: acoustical tiles, boards, and sheets; acoustical plasters and sprayed-on plastic
materials^ mineral wool, Fiberglas blankets, and acoustical felts; set materials for use in
motion-picture studios; hangings, floor coverings, and miscellaneous materials; hard
plasters, masonry, wood, and other standard building materials; and audience, individual
persons, chairs, and other objects. The tabulation in each group of materials is arranged
in alphabetical order.
24. PRACTICAL CONSIDERATIONS OF SOUND-ABSORPTIVE
MATERIALS
In making a choice of absorptive materials a number of other factors must be considered
besides the coefficients of sound absorption. Good acoustics is only one of many qualities
which should be secured in every building. Thus, besides absorption coefficients, it is
necessary to consider such factors as the following: structural strength; decorative pos-
sibilities; adaptability to the surface available for, or requiring, absorptive treatment;
maintenance; sanitation; ease of application; fire hazard; absorption of water; attraction
for vermin; "fool-proof ness"; durability; and cost. Each room requires a certain amount
of sound absorption; certain surfaces in some rooms require highly absorptive treatment.
These two conditions usually limit the choice of absorbents to materials having coeffi-
cients within certain specified limits. As a rule, however, many materials having coeffi-
cients within these limits will be available. This allows considerable freedom hi the selec-
tion of materials which will be satisfactory not only acoustically but also for the other
requirements. For a detailed discussion of the choice of sound-absorptive materials
consult any standard textbook on architectural acoustics (as Knudsen and Harris, Acous-
tical Designing in Architecture).
For bibliography, see p. 12-76.
SOUND INSULATION
By Vern O. Kncdsen
25. NOISE MEASUREMENTS
During recent years, acoustical engineers and civic authorities have become increasingly
aware of the problems associated with the measureme^it and abatement of noise. One of
the prime requirements for good acoustics in every room is absence of noise, i.e., unwanted
sound. In the design of theaters, music rooms, churches, schools, office and industrial
buildings, hotels, apartment houses, and studios for the recording or broadcasting of
sound, it is necessary that the designing architect or engineer know (1) the amount aad
kind of the noise against which he is to provide insulation, and (2) the amount of noise
which can be tolerated in different types of buildings. The difference between the mag-
nitudes of (1) and (2) gives the amount of sound insulation which should be provided in
the building. As -discussed in article 5 of this section the magnitudes of noises vary over
a wide range.
The magnitude and character of steady sounds can be represented by plotting the
intensity level (per cycle or for a specified band width) as a function of the sound frequency.
In Fig. 1, the intensity level per octave, i.e., the intensity levels as measured in octave
bands, for a number of ordinary sounds are plotted for the important audio-frequency
range of 50 to 10,000 cycles. Traffic noise will be seen to have its predominant intensity
12-58
ACOUSTICS
at low frequencies; the noise from typewriters, on the other hand, is greatest at high fre-
quencies. Such characteristics of noise should be considered in the problems of sound
insulation and noise reduction in building design.
Most measurements of noise, of interest in building design, have been made with com-
mercial sound-level meters which measure the overall sound level in decibels rather than
the intensity level as a function of the frequency. The latter should be used whenever
available, but the sound level corresponds roughly with the sensation of the sound and
provides a convenient numerical scale for comparing the levels of different sounds. Thus,
Fig. 2 gives the average sound levels, in decibels, as measured with a sound-level meter,
for ajlarge number of locations in or near buildings.
90,
8 "
1570
1^60
i 50
40
^
1 1 I 1
^
\ \
V
T 1 I 1
50
1OO
200
5,000 10,000
500 1,000 2,000
Frequency (cycles per second)
FIG. 1. Sound Spectra of Some Typical Noises. (Fleming and Allen.) (British Crown Copyright
reserved. Reproduced by permission of the Controller of His Britannic Majesty's Stationery Office.)
Examples of Noise Analysis
A — Traffic noise. Average of miscellaneous vehicles passing at about 20 ft.
B — Typists' room. Two typewriters in operation.
C — Woodwork shop. 14-in. circular saw.
D — Woodwork shop. Planing machine.
If a sound wave completely modulates the pressure of the air at sea level, i.e., if the
instantaneous pressure varies from 0 to 2 atmospheres, the intensity level would be 194 db.
This represents an upper possible limit for the intensity of sounds, a limit which is not far
above that actually attained with the Victory Siren (a large air stream modulated with a
1 'chopper"), which was used in New York City and other American cities as an air-raid
alarm during World War II. Most of the other entries in Fig. 2 are self-explanatory. The
standard deviations are given for a number of measurements; these were made by Bell
Telephone Laboratories (D. F. Seacord, J. Acoits. Soc. Am., Vol. 12, 183) at more than
600 locations in four different cities. The measurements hi the private hospital room
(made by the author with a continuous recorder) revealed sound levels of 50 to 58 db dur-
ing 80 per cent of the time from 5:00 P.M. to 7:00 P.M.; at 9:00 P.M. the level had dropped
2 or 3 db. In the corridors of this same hospital, levels of 65 to 75 db were common; there
were peak levels of 78 db from the closing of elevator doors 55 ft away from the sound-level
recorder, and 90 db from coughing 40 ft away.
26. ACCEPTABLE NOISE LEVELS IN DIFFERENT BUILDINGS
Although it is not customary for building codes to specify the allowable noise in dif-
ferent types of buildings, and opinions differ considerably as to tolerable noise levels, the
following table gives approximate loudness levels which will be, in general, highly satis-
factory:
Decibels
Radio, recording and television studios 25 to 30
Hospitals " " 35 to 40
Music rooms 30 to 35
Apartments, hotels, and homes 35 to 45
Theaters, churches, auditoriums, classrooms, and libraries 30 to 40
Private offices and conference rooms 35 to 45
Large public offices, banking rooms, stores, etc 45 to 55
Restaurants 50 to 55
Factories 45 to 80
NOISE LEVELS IN DIFFERENT BUILDINGS 12-59
Special conditions or circumstances, such as past experience, other near-by noises, and
costs, may alter the acceptable noise levels, but the levels given in the table are recom-
mended for purposes of building design. As will be seen by comparing these values with
those given in Fig. 2 the acceptable values given in the table are somewhat lower than
Noise Out-of-doors
Deci-
bels
Noise in Buildings
30 ft from Victory Siren (assuming a 50-kw
sound source and n<> ft+tftrnijtflon) >
-200-
Complete modulation of air pressure at sea level
Test chamber for airplane motors (l50Q-hp*
propeller type)
Very noisy electric power substation
Subway station, express train passing
Electric power sjubstatkm (about average)
Ventilating and eqalpment room for large note!
Average factory (standard deviation =12 db)
Kaiser William Memorial Church.. Berlin (usuaj
daytime traffic)
Large offices (standard devIailon—4.5 db)
Large stores (standard deviations*: 6.0 db)
Private room, hospital, on WUshlre Boulevard,
Los Angeles
Average residence, with radio (standard deviation—
, 8.0 db)
Average residence, without radio (standard delation
-5.5 db)
Average church
Theater, no audience, quiet location
Quiet suburban residence, at night, no near-by
traffic
Quiet sound studio for making motion pictures
Reverberation room, University of California
at Los Angeles
-180—
—160-
—120-
Nolse from 4-motor transport alcplane, • >
2000 ft overhead
Heavy automobile traffic on WHshke Boulevard, — >•
Los .Arjgeles
—lOCh^
—80 —
—60—
HoJIywood Bowl,early evening, no audience present-*-
= 4O—
—20—
— 0 —
FIG. 2. Sound Levels in or Near Buildings
those that prevail in existing buildings. The average loudness level in the private hospital
room, for example, is 54 db, which is some 15 to 20 db greater than the level proposed in.
the table. Since the outside traffic noise adjacent to this hospital has an average level,
when traffic is heavy, of 80 db, and since the average tolerable level for a hospital is 37 db,
the building should be designed for sound insulation in such a manner as will provide an
overall noise reduction 80-37 db, i.e., 43 db. Part of the required noise reduction can be
accomplished by a proper "setback" of the building and, in some instances, by dense
planting of evergreen shrubs and trees between the street and the building; another part,
by the use of sound-absorptive materials within the building; but most of the reduction
can be accomplished only by proper sound insulation of the building itself.
12-60
ACOUSTICS
27. FUNDAMENTAL PRINCIPLES OF SOUND INSULATION
Nearly every building is subject to the annoyance of noises which have their origin in
adjacent rooms or outside. It is possible to design buildings in such a manner as to ex-
clude effectively both these types of annoying noises. The principal means whereby such
noises enter a building are the following: |
1. By means of openings, as windows, cracks around doors, ventilating ducts, or any
other openings that will admit a free flow of air.
2. By means of refraction or transmission through partitions. This is analogous to the
refraction or transmission of light from air to water, or between any other two dissimilar
media.
3. By means of the conduction of sound through solids. For example, "impact sounds,"
such as footfalls, hammering on walls or floors, or the moving of furniture on hardwood
floors, are conducted through the dense and rigid structural members of a building.
4. By means of the diaphragm action of walls which communicate sound from one side
of a partition to the other side.
.l/'-J-M
Isolation Felt
One Design of
Johns-Manvllle
Floor Chair
Furring Channel
.Metal Latb
Plaster
J-M Wall
Isolator
.Tie Wires
•Wood Ground
-Wood Sleeper
I-M Floor Chair
Typical JohnszManville Wall Isolating Treatment
Typical
Johns-Manville
Ceiling Isolator
As Used by United States Gypsum Co.
FIG. 3. Flexible Cushions, Supports and Connectors
The refraction or transmission of sound from one medium to another, as from air to
plaster or stone, is an almost negligible factor in building construction — not more than
about one-millionth of the intensity of the incident wave in air can penetrate a material
like brick or stone.
The transmission of sound through openings, on the other hand, is often the means by
which sound is most readily transmitted from one portion of a building to another. This
means of transmission often limits the amount of sound insulation which can be obtained
in buildings, especially in hotels and apartments where the insulation is determined by
such unavoidable openings as may be incidental to the use of windows and doors. Under
such circumstances it would be futile to provide a relatively high insulation through the
se|>&rating walls or partitions. Even very small openings, such as cracks around doors
or around imperfectly fitting windows, are effective in transmitting a considerable amount
of sound.
FUNDAMENTAL PRINCIPLES OF SOUND INSULATION 12-61
The transmission of sound through ventilating ducts often becomes & troublesome prob-
lem. There are three types of sound-transmission which must be controlled: (1) the noise
from the fans, motors, and other air-conditioning equipment which is transmitted through
the ducts and into the room; (2) the noise from an adjacent room which is transmitted
from opening to opening, ^ of ten through a short and highly conductive section of duct;
and (3) the noise from adjacent rooms- or outside which may be transmitted through the
walls of the duct and thence
through the ducts and into the
room. The noise from the ven-
tilating equipment room can be
reduced suitably by (1) the
selection of slow-speed, quietly
operating equipment; (2) treat-
ing the walls and ceiling of the
equipment room with highly
absorptive material; and (3)
introducing acoustical attenua-
tion within the ducts, which
W/y/w#2&3^^
M
can be accomplished by using FlG* 4* m***™ Method for Insulation of Vibration
very long ducts of small cross-sectional area and by lining the ducts with highly absorptive
material, or by introducing other acoustical filters in the ducts.
Solid-borne sound travels through the structural members of a building with but very
little attenuation. The compressions! wave in a solid is often communicated to large
surfaces, as the walls or floor of a room, and these large surfaces are made to vibrate like
the sounding board of a piano. In this way a large portion of the solid-borne sound may
be radiated into a room. Many solid-borne sounds can be controlled by the carpeting of
floors; by the wrapping of pipes — especially where they touch the frame of the building —
with flexible, porous materials, as hair felt; or by the proper mounting of machinery on
flexible or elastic supports, so that the natural frequency of the machinery mounted on its
flexible support will be low in comparison with the frequencies which are to be insulated.
One of the most effective methods of eliniinating these solid-borne sounds is to introduce
discontinuities in the paths of the conducted sounds. These discontinuities should consist
of materials which differ largely in elasticity and density from the solid structure of the
building. For example, it is possible to suspend the ceiling by means of flexible supports;
it is possible to build up inner walls in a room which are fastened to the monolithic frame
by means of flexible ties; and it is possible to float the floor of the room upon flexible pads
of cork or felt or other elastic material. In Fig. 3 are shown two types of flexible cushions,
supports, and connectors which are effective for insulating solid-borne vibrations in
buildings. Figure 3 also shows some constructional details for insulating solid-borne sound
in buildings.
Figure 4 shows a simple method of insulating any object, as a part of a building or a
piece of equipment, from earth, building, or machinery vibration. The problem consists
of insulating a mass TO from another object of mass M by means of a flexible support
which has certain elastic and damping properties, Figure 5 is the electric circuit equivalent
M
o
o
o
o ^^
o
o
o
FIG. 5. Electric Circuit Equivalent of Fig. 4
of Fig. 4. This circuit implies that, when M is set into forced periodic vibration, these
vibrations are communicated to m principally by means of the elastic coupling between
M and m, although the internal damping or resistance r of the system also contributes to
the coupling. If ai and 03 represent the amplitudes of vibration set up in M and m,
respectively, n the frequency, and c the compliance, then
* -f
[2irmn — (l/2irnc)P
(1)
12-62
ACOUSTICS
This equation has been tested experimentally for both supported and suspended systems
and is in good agreement with the observed results. The equation is useful for calculating
the insulation value of different types of flexible supports. For values of n which are
small compared with the natural or free vibration of m upon its elastic support, a2M will
be equal to unity; that is, m and M vibrate with the same amplitude. At the resonant
frequency, a2/ai is greater than unity, or the insulating support actually amplifies the
motion imparted to m. However, at frequencies greater than — Vmc the value of
becomes less than unity, and it approaches the value r/Z-n-nm at frequencies which are
high compared with the natural or resonant frequency. In general, both m and c should
be as large as possible if m is to be well insulated from the vibrations in M; that is, the
support should be very elastic and loaded as heavily as possible (see also article 30) .
In Table 1 are given the values of the compliance c and the resistance r of a number of
materials which are used for the insulation of vibration. Beside these materials there are
a number of patented devices, similar to those shown in Fig. 3, which are very effective.
(See Sound Transmission in Buildings, by Fitzmaurice and Allen, His Majesty's Stationery-
Office, London [1939], and Modern Theory and Practice in Building Design, by Fleming
and Allen, The Institution, London [1945].)
Table 1. Compliance and Resistance Data for Typical Specimens of Flexible Materials
The compliance and resistance given in the table are for specimens 1 in. thick and 1 sq cm in cross-
section.
Material
Description of
Material
Approximate
Upper Safe
Loading, Ib
per sq in.
Compliance,
c, cm per
dyne
Resistance,
r, absolute
units
Corkboard
1. 10 Ib per board ft
12
0.25 X 10~6
0.15 X 105
0.70 Ib per board ft
8
0.50 X 10~6
0.25 X 105
1 . 35 Ib per board ft
4-6
0.60 X 10~6
0.50 X 10s
Celotex
Insulating board
12
0.18 X 10~6
Insulating Hr»ar(J
15
0.16 X 10~6
^lasonite . . . « .
Tnsnlfiting Tx>ftT-d
15
0 1 2 X 1 0~6
Sponge rubber . .
25 Ib per cu ft
1-3
3.0 X 10~6
55 Ib per cu ft
3-6
1.2 X 10~6
Hair felt
1 0 Ib per cu ft
'1-2
1.5 X 10"6
In the choice of materials for the insulation of vibration or solid-borne sound, it is
necessary to give consideration to the safe amount of loading the material will withstand
without breaking down or without being compressed to the extent that its compliance is
reduced beyond required limits. It also is important to select a material that will have a
long life and that will not continue to compress or settle under the load which it supports.
For example, if ordinary insulation cork is loaded as much as 20 or 30 Ib per sq in., the
material will continue to compress indefinitely, and at the same time will become less
and less compliant, until ultimately it not only loses its insulation value but also allows
an amount of settling which cannot be tolerated. For example, a specimen of 1-in. insula-
tion cork (0.70 Ib per board ft), under a load of 20 Ib per sq in., settled 0.04 in. during the
first 24 hours, 0.02 in. during the next 24 hours, and 0.11 in. during the first 5 months it
was under compression. The same specimens, under a load of 10 Ib per S& in., settled only
0.01 in. during the first 24 hours, 0.005 in. during the next 24 hours, and only 0.03 in.
during the first 5 months. In general, the most satisfactory material will be one that has
a high compliance and very little tendency to settle under the influence of the load and
that tends to return to its initial condition when the load is removed. Hair felt, cork, and
rubber seem to be the best available materials that meet these requirements, although all
these materials continue to settle, and become less and less compliant, as they become
older. Flexible steel supports and clips, such as those shown in Fig. 3, do not have these
defects and are proving to be very satisfactory not only for the insulation of walls, floors,
and ceilings but also for insulating all sorts of equipment from the floor or the rigid frame
of the building.
INSULATION OF SOUND BY POROUS MATERIALS. The insulation of sound by
porous materials is accomplished principally by viscous losses within the capillary pores
within the material and by the vibration of the component parts of the material. Fig-
ure 6 shows the transmission coefficients at different frequencies for one, two, three, and
four layers of hair felt having a density of 12 Ib per cu ft. These results show that, approxi-
mately, the logarithm of the energy reduction, or the reduction in decibels, of sound
FUNDAMENTAL PRINCIPLES OF SOUND INSULATION 12-63
0-5
02
o-i
OO5
transmitted through porous materials is proportional to the thickness of the material.
The results also show that porous materials, if used by themselves, do not provide a very
high degree of sound insulation unless the insulating blanket or partition is very thick.
Thus, at 700^ cycles, the coefficient of transmission for four layers of hair felt— each layer
is 0.58 in. thick — is about 0.01; that is, a sound wave of 700 cycles would be attenuated
only 20 db in passing through 2.32 in. of hair felt. However, when such materials are
used properly in conjunction with rigid partitions, they may contribute a considerable
amount to the total insulation sup-
plied by a wall structure. One of I -Or
the most effective ways in which
such materials may be used for the
insulation of sound is by suspending
or supporting the porous blanket in
an air space between two rigid par-
titions.
INSULATION OF SOUND BY
RIGID PARTITIONS. Sound is
transmitted through rigid partitions
principally by the forced vibration
of the wall; that is, the entire parti-
tion is forced into vibration by the
pressure variations of the incident
sound wave. The transmission co-
efficient T for a heavy partition, as
masonry or concrete, for normally
incident sound, is given, approxi-
mately, by
0-02
o-oi
where pi and ci are the density and
sound velocity in the partition, p
and c the corresponding density and
velocity in the air, ki = STT/XI, where
Xi is the wavelength of the sound in
the partition and I is the thickness
of the panel. The transmission loss
in decibels (10 logio 1/r) for a 9-in.
brick wall, as calculated by eq. (2),
is about 50 db at 100 cycles and
0-005
0-ooz
O-OOl
400
1200
1600
600
Frequency
FIG. 6. Transmission Coefficient for One, Two, Three,
and Four Layers of TTflir Felt. (Davis and Littler.)
rises almost uniformly with frequency to 78 db at 4000 cycles, and then drops to a
minimum at 8000 cycles (which is zero according to eq. [2] but actually is of the order of
50 db because of dissipation within the partition). At frequencies below about 100 cycles,
the resonant properties of the partition are of considerable influence; the transmission
loss (T.L.) at these low frequencies may be much less than that calculated by eq. (2).
The observed T.L. for heavy masonry partitions, even at 100 to 4000 cycles, is some 10 to
15 db less than that calculated from eq. (2), but the equation is useful for predicting the
influence on T.L. of such factors as the wavelength of the sound and the mass and thick-
ness of the partition.
For most rigid walls in buildings, as concrete, brick, clay or gypsum tile, wood or metal
studs plastered on one or both sides, and even glass or metal panels, eq. (2) can be further
simplified so that, approximately, for frequencies of 100 to 4000 cycles,
?) (3)
where k = 2?r/X (X is the wavelength of the sound in air) ; and TO is the effective mass per
unit area of the wall, which is of the order of 0.2 to 1 times the actual mass per unit area.
The mass reaction of rigid walls is thus the dominant factor affecting sound transmission;
the sound is transmitted largely by the diaphragmlike vibration of the wall, the wall re-
sponding to the alternating force of the impinging sound wave much as a rigid piston would.
In thin flexible panels, the stiffness, the internal damping, the size of the panel, and the
manner in which it is clamped around the edges all contribute to the total amount of vibra-
tion which will be imparted to the partition, and therefore all these factors contribute to
the insulation value of such walls. However, these factors are effective principally at low
frequencies; the mass is the predominant factor throughout most of the audio-frequency
12-64
ACOUSTICS
range in determining the insulation value of nearly all rigid panels and partitions encoun-
tered in practice. In Fig. 7 is given a summary of the measured insulation value of many
rigid panels having weights varying from 2 Ib per sq ft up to 100 Ib per sq ft. There is a
nearly linear relation between the average T.L. and the logarithm of the weight per square
foot of the partition. (The average T.L. is the arithmetical mean of the measured trans-
mission losses at 128, 256, 512, 1024, and 2048 cycles.)
Whereas the insulation value of porous materials is proportional approximately to the
thickness of the material, the insulation value of a rigid material increases only as the
logarithm of the thickness. Because of the slow increase in insulation with increased mass
or thickness of a rigid partition, it is not always feasible to secure a high insulation by
merely increasing the thickness of the wall. Thus, it would be necessary to increase the
thickness of a concrete wall to nearly 4 ft hi order to give the wall an insulation of 60 jib.
60
55
35°
| 45
i 4°
1 35
30
25
20
A Bureau of Standards
0 Knudsen
. « Meyer
X Nat. Phys. Lab.
A °
o
X
^
****
A
"
0
-"""on
a
o
0
**
^****°
a
o A
^
+**
**
^^**
^-^
^^*
o
--^
2 3 4 5 6 7 8 9 10 20 30 40 50 607080901
Weight per Square Foot
FIG. 7. Transmission Loss in. db for Rigid Single Partitions
When walls of high insulation are required, it is more feasible and- economical to employ
special structures which combine the two principles of sound insulation just described:
namely, absorption losses in porous-flexible materials, and inertial losses in massive parti-
tions. Thus, two or three rigid and relatively thin partitions separated from each other
by felts or blankets can easily be composed- in such a manner as to give an insulation of 60
or even 70 db. The insulation value of many special forms of construction employing
these and other principles will be found in the tables in the next section. (See also ref-
erences given on p. 12-75.)
28. COEFFICIENTS OF SOUND TRANSMISSION
The coefficient of sound transmission of a panel is the ratio of the transmitted to the
incident sound energy. One of the most satisfactory methods for measuring the coeffi-
cients of different materials is to make measurements of the sound intensity on both sides
of a test panel placed between two rooms which are so constructed that no sound is trans-
mitted from one room to the other except through the test panel. Thus, suppose the aver-
age intensity near the panel in the source room to be 1 1 and the average intensity hi the
test room to be Ii. Then the rate of flow of sound energy against the test panel in the
source room will be I\A, where A is the area of the test panel. The rate at which energy
will be transmitted through the panel into the test room will be I\Ar, where r is the trans-
mission _ coefficient for the panel. The product IiAr is then the rate of emission of sound
energy in the test room. Hence, when equilibrium is established, this rate of emission of
sound energy will be equal- to the rate of absorption of sound in the test room, which ia
equal to I^a, where az is the total absorption of the test room. Hence,
IiA
(4)
The coefficient of transmission thus involves not only the intensities on the two sides of
tfee panel but also the area of the panel and the total amount of absorption m the test
room,
COEFFICIENTS OF SOUND TRANSMISSION
12-65
Table 2. Coefficients of Sound Transmission
Description of Panel
(Bold-face type signifies
that the panel has
practical merit)
Weight,
Ibper
sq ft
Reduction Factors in Decibels
Au-
thor-
ity
Prob-
able
Aver-
age
T.L.,
db
Probabte
Average
Value
of r
128
256
512
1024
2048
Porous-flexible Materials and Fiber Boards
Celotex, Standard, 0.5 in..
0.66
22.4
17 3
23 4
27 4
1 *
20
0 010
Insulite, 0.5 in
Hair felt, 1 in
0.75
0.75
4 9
22.2
4 6
20.2
6 0
24.1
7 I
20.9
6 7
I*
3
19
0.013
Hair felt, 4 in
7.5
12.5
15 3
19 7
19 4
3
Rock Wool blanket, 0.5 in.
covered on both sides
with heavy brown paper
TJpson Blue Stripe Insula-
tion
15.5
14.0
15.1
17.8
16.0
18.5
18.4
21. 1
2
2
16
16
0.025
0.025
Thin Rigid Materials
Aluminum, 0.025 in.
Duralumin, 0.020 in
Iron, 0.03 in. galvanized . .
Lead, 0.062 in
0.35
0.33
1.2
3 9
17.9
14.1
25.3
31 ft
13.2
12.5
20.5
33 2
17.7
17.6
28.8
32 0
23.2
22.5
35.0
32 I
I *
1 *
1 *
1 *
16
15
25
30
0.025
0.032
0.0032
0 0010
Plywood, 0.25 in., three-
ply
0.73
21.0
20 7
25 5
26 0
I *
21
0 OO&G
Mahogany, 1.85 in
4.9
26.0
27 0
36 0
4f
28
0.0016
Plaster board, 0.5 in
27.0
28.0
33.0
28
0.0016
Doors and Windows
Doors
Birch veneer, light, four
panel. . .
13.0
16 1
20 4
22.8
22.0
3
22
0.0063
"Cold-storage" door,
double wall, 4 in. ......
16.4
20.8
27.1
29.4
28.9
3
29
0.0013
Oak, solid, 1175 in., with
cracks as ordinarily hung
11.5
15.1
20.4
22.0
16.2
3
20
0.01
Oak, like above, well seas-
oned and air tight
15.1
18.2
22.8
25.7
25.2
3
25
0.0032
Steel, solid, 0.25 in.
25.1
26.7
31.1
36.4
31.5
3
35
0.00032
Window
T5
Glass, plate, 0.25 in
Glass, plate, 0.25 in., four
panes
3.5
23.2
32.6
20.8
30.9
26.4
33.5
27.5
34.2
22.8
1*
3
30
29
0.0010
0.0013
Glass, plate, 0.25 in.,
double glazed, 16 in.
separation
43. Ql
3
48
0.000016
Rigid Partitions (Tile, Brick, Concrete, etc.)
Brick panel, 8 in.; plas-
tered both sides
97.0
47.7
49.4
57.0
59.2
1*
49
0.500013
Tiles, hollow-clay parti-
tion, three cells, 4 in. by
12 in. by 12 in., plas-
tered both sides
29.0
41.1
40.0
41.5
49.9
1 *
40
0.00010
Tile, hollow clay, 4 in.,
unplastered .......
17.0
24.5
24.1
26.1
35.5
29.8
3
35
0.00032
Tile, like above, 0.5 in.
plaster . ...........
22.0
25.1
24.3
26.9
38.2
33.9
3
38
0.00016
Tile, hollow gypsum, 3 in,,
unplastered .....
11. 1
19.2
18.7
20.8
28.5
30.0
3
31
0.00080
Brick 4.5 in., 0.5 in. fiber
board stuck on each face,
then 0.6 plaster on each
faee
46.8
44.
45.
51.
73.
6
48
0.000016
Brick, 0. 25 in. Masonite on
lath on one side, 11 in. ,
88.0
36.5
37.0
48.0
58.5
61.0
5§
48
0.000016
12-66
ACOUSTICS
Table 2. Coefficients of Sound Transmission — Continued
Description of Panel
(Bold-face type signifies
that the panel has
practical merit)
Weight,
Ibper
sqft
Reduction Factors in Decibels
Au-
thor-
ity
Prob-
able
Aver-
age
T.L.,
db
Probable
Average
Value
of T
128
256
512
1024
2048
Rigid Partitions (Tile, Brick, Concrete, etc.)— Continued
Clinker concrete, 3 in.,
plastered both sides
Concrete, 3 in.; 0.75 in.
cement and linoleum . . .
31.
49.0
28.
36.5
33.
37.5
40.
44.5
50.
54.0
57.
65.0
6
5§
40
48
0.00010
0.000016
Wood Studs and Plaster, Metal Channel Iron and Plaster, etc.
Wood studs, 2 in. by 4 in.,
17in.o.c.,0.25in.by 1.5
in. wood lath, 0.375 in.
apart, gypsum scratch,
lime brown, smooth fin-
ish
49.5
42.6
32.2
46.6
43.7
52.2
35.7
42.9
36.7
1 *
3
3
3
44
37
43
40
0.000040
0.00020
0.000050
0.00010
Wood stud; wood lath,
0.25 in. by 1. 5 in. spaced
0.375 in.; gypsum
scratch coat, 0.25 in.;
brown coat, 0.25 in.—
0.375 in.; finish coat
Wood studs, etc., as above
except lime plaster
18.6
18.0
12.0
24.4
27.5
17.7
25.6
28.8
24.7
29.1
38.1
37.0
Wood studs, 2 in. by 4 in.,
0.5 in. Celotex, gypsum
plaster
Floor and Ceiling Partitions
Concrete flat slab floor
construction, reinforced.
Insulite furred out, ap-
plied as ceiling
54.4
50.9
54.8
58.7
56.5
53.2
1 *
51
0.0000080
Wood joists. Lower side
plastered on wood lath;
upper side, subflooring
and 0.375 in. finish floor-
47.9
46.8
40.7
50.1
48.8
1 *
43
0.000050
Wood joists, etc., as above,
with floating floor con-
sisting of nailing strips
rough and finish flooring
57.6
57.5
54.8
62.4
57.6
1 *
53
0.000005
Double Walls
Tile, double 2 in. solid gyp-
sum, unplastered, un-
bridged, 2 in. separation;
structurally separated . .
20.4
25.2
34.2
44.5
51.0
62.6
3
48
0.000016
Tile, etc., as above, except
bridged, at middle
20.4
21.3
32.7
37.0
45.6
52.0
3
44
0.000040
Tile, etc., as above, filled
with sawdust
23.0
21.6
28.1
39.3
47.0
54.0
3
44
0.000040
Tile, double 2 in. solid gyp-
sum, unplastered, un-
bridged, 4 in. separation;
structurally separated . .
20.4
28.4
47.4
54.2
59.0
56.8
3
51
0.000008
* Reduction factors from the Bureau of Standards, for the most part, are for the following frequency
bands: 150 to 157, 250 to 285, 500 to 547, 1000 to 1070, and 20OO to 2175 cycles. The data for the
several frequency bands are recorded under the frequencies to which the frequency bands most nearly
correspond.
t For frequencies of 300, 500, and 1000 cycles.
t Average value from 128 to 2048 cycles.
§ Berg and Holtsmark's reduction factors are for frequency bands of 100-200, 200-400, 400-800,
800-1600, and 1600-3200 cycles. Their values are recorded under 128, 256, 512, 1024, and 2048 cycles,
respectively.
Authority: (1) Bureau of Standards, (2) V. O. Knudsen, (3) P. E. Sabine, (4) Davis and Littler,
<5) Berg and Holtsmark, and (6) National Physical Laboratory.
CONSIDERATIONS IN SELECTION OF MATERIALS 12-67
For other methods of measuring transmission coefficients see Knudsen, Architectural
Acoustics, Chapter XI.
The results of sound-insulation measurements obtained in different laboratories axe
grouped in Table 2. Each group contains the data for materials or partitions having a
number of properties in common. The data in each group have been arranged so as to
keep together those from each laboratory, which is necessary since the results on the same
panel tested in different laboratories are not always in good agreement. The data from
most laboratories give what has been called the reduction factor for the panel or partition
tested. This reduction factor is usually the ratio of the intensities of sound on both sides
of ^ the test panel, or, in decibels, is 10 times the logarithm of this ratio. Since the trans-
mission coefficient depends upon the size of the panel and the amount of absorption in
the test room, as is shown by eq. (4), the reduction factors published by several labora-
tories (before about 1935) do not agree with the T.L., which in decibels is 10 logie 1/r. The
compiler has made an attempt to adjust the data from different laboratories in such a
manner as to give comparable ratings for all the materials and partitions listed in the tables.
In the table, the data given under "Reduction Factors in Decibels" are the results
published by the authors. The data given in the last two columns in the table give the
compiler's estimate of the probable average value of the T.L., and the probable average
value of the transmission coefficient r. The reduction factors at the different frequencies
are useful since they describe the insulation value of the panel or partition at these fre-
quencies. This is often an important matter in the selection of materials or partitions
for sound insulation. For example, partitions which have a relatively low insulation
value in the frequency range from 500 to 1000 cycles would not be suitable for the insula-
tion of traffic noise and of most noises met in buildings, since most such noises contain a
relatively large amount of sound energy in this frequency range. (See Fig. 1.) For this
reason, the panels which show the highest values of T.L. may not supply the greatest
amount of sound insulation for all types of noise. It is necessary, in determining the best
type of partition for each problem which arises in sound insulation, to give consideration
to the reduction factors at the different frequencies as well as to the average value of T.L.
or r.
Partitions which possess outstanding merit with regard to both insulation value and
practicability are designated by bold-face type in the column which gives the name and
description of the partition,*
29. PRACTICAL CONSIDERATIONS IN THE SELECTION OF
MATERIALS AND TYPES OF STRUCTURE FOR
INSULATION IN BUILDINGS
Since errors as large as 3 or 4 db are inherent in many of the data on sound insulation,
small differences in the tabulated results of the preceding article should not be regarded
as having much significance. A consideration of the tabulated data suggests the following
generalizations concerning the insulative properties of different building materials and
partitions :
1. The insulation value of rigid masonry or monolithic partitions increases directly as
the logarithm of the weight per square foot of wall section — so that the rate of increase of
insulation with increased weight is relatively slow for partitions which are heavier than,
say, 30 or 40 Ib per sq ft. As a consequence, it is often in the interest of both insulation
and economy to substitute two or more light-weight partitions, or specially composed
partitions, for heavy masonry partitions. There are many occasions in building practice
where this may be done with a gain in insulation, with, a reduction in the dead load of the
building, and at a reduced cost. However, for thin partitions, where the dead load is not
a serious problem, dense rigid panels such as plastered brick or solid tile provide a satis-
factory means of obtaining a T.L. of about 40 to 45 db.
2. Lime plaster on wood lath and wood studs gives better insulation than an equal
thickness of gypsum plaster on wood lath a-rtrl wood studs. Sabine reports an advantage
of about 9 db for lime plaster as compared with gypsum plaster, and the Bureau of Stand-
ards reports an even greater difference. Wood stud and plaster partitions rate slightly
higher than channel iron and plaster.
3. Wood partitions* with tongue-and-groove joints, provide more insulation than
masonry partitions of the same weight or thickness. (The development of cracks in wood
partitions, however, will greatly reduce their insulation value,)
* More extensive tables on sound-insulation data will be found in Knudsen's Architectural Acoustic**
Glover's Practical Acoustics for the Constructor, Constable and Ashton, Sound Insulation of Single and
Complex Partitions, Philosophical Mag., Vol. 23, 161-181 (1937) , and Knudsen and Harris, Acoustical
Designing in Architecture (1949).
12-68
ACOUSTICS
4. Double partitions seem to offer the most feasible means of obtaining high insulation
at a reasonable cost and reasonable dead load. The separate partitions should be as com-
pletely insulated from each other as possible, as the introduction of structural ties between
the separate partitions tends to convert the two partitions into a single rigid one and thus
greatly reduces the insulation. The suspension of a blanket or fiber board between double
partitions or between the wood studs or channel irons in staggered stud partitions is often
•8 Brick
I
m\ T.L-49d6
H— 3wHoIIow Clay Tile
T.L.=40dd
- 4HoHow Clay Tile
""l"x2"Furring Strips
'Paper and Metal Lath
"Gypsum Plaster
T.L=52<Z6
-% Steel Channels
-^'Plaster
Gypsum: T. L»34dZ>
Lime .• T. L. =40 db •
Gypsum Scratch Coat
-*" Lime Brown and Finish
—Wood Lath
\ 2\ 4"Wood Studs
-2"x 4*Wd Stud*
-Sheet Metal
*-3 Coat Gypsum
T.L-45d6
ough aiid Finished Flooring
ood Nailing Strips
Concrete Slab
re Board and Plaster
-Rough and Finished Flooring
•Wood Nailing Strips
"Hollow Clay Tile
Vibre Board and Plaster
.Floated Rough and Finished
Flooring
2x 10 Wood Joists
Plaster on Wood Lath
-4*HoHow Clay Tile
-l"x 2" Furring Strips
'1$ Fibre Board
-Gypsum Plaster
T. L— 54 db
.2x4 Wood Studs
. t Fibre Board,
Joints Filled
} Coat Gypsum
T.L=49d6
.-Rough and Finished Flooring
-Absorptive Blanket
Plaster on Wood Lath
T. L.>50 db Good Insulation for
Fool Falls, etc,
-3 Solid Gypsum Tile
" Plaster
-4 Brick
-%*PIast«
Staggered Wood Studs
-Absorptive Blanket
-Plaster on Fibre Board
T,L>50d6
2 Layers J/Mutex with
Sheet of 28 Gauge
Iron between
—3 Masonry
-*- Plaster
T. L>60 db
T, L -47 db JUfn Acous. Corp. of America
Double Masonry Wall
T. L=>60 db
FIG. 8. Recommended Types of Structure for Sound Insulation
Rough and Finished Flooring
Ji' Fibre Board
oncrete Slab
Hung Ceiling
Flexible and Absorptive
Material
Resilient Chair
Concrete Slab
Resilient Hanger
Plaster and Lath
U. S. Gypsum and
Johns-Manville
System
an aid to insulation. The addition of any absorptive material in the air space between
double partitions contributes considerably to sound insulation unless the absorptive
material makes a rigid or semirigid bridge between the two partitions, hi which case it
may be worse than nothing. Thus, the addition of cinders, pumice, or other rigid-porous
materials between structurally separated partitions will sometimes reduce the overall
insulation. *
A number of satisfactory types of construction for obtaining wall partitions having a
T.L. greater than 40 db and floor and ceiling partitions having a T.L. greater than 50 db
are indicated in Fig. 8. These methods of construction will meet most of the requirements
lor sound insulation that will arise in connection with the design of buildings. The aver-
age TX. is given for each partition. (See also references given on pp. 12-67 and 12-75.)
THE HEARING OF SPEECH IN AUDITORIUMS 12-69
30. CALCULATION OF INSULATION IN BUILDING DESIGN
From a simple consideration of the transmission of sound through the boundaries of a
room it can be shown that the noise-reduction factor for a room (the number of decibels
the intensity of the sound is reduced by transmission through the boundaries) is given by
Noise-reduction factor = 10 logw 7
(5)
where a is the total absorption of the room, and T — r\A\ + rzA* -f- -riA* + . . . is the
total transmittance for th,e boundaries of the room. TI, TS, and ra are the coefficients of
transmission of the different parts of the boundaries of the room, and J.i, A^ and A* are
the corresponding areas of these boundaries.
In order to illustrate the use of eq. (5) a typical calculation will be made for determin-
ing the noise-reduction factor of a small studio.
Volume of room = 50,000 cu ft.
Total absorption in room, including audience = 2400 sabins.
Description of Walls, Ceiling, Windows, and Boors; and the Transmittance through
These Surfaces
Material
Area, At
sqft
T
rA
4-in. concrete slab ceiling plus 1/2 in. acoustical
2500
0.000025
0.0625
8~in. brick walls plus V9 in. acoustical material. .....
4500
.0000080
.0360
3/ig-in. glass windows, closed
400
.00110
.440
} 1/o-frj, hardwood <^f>ors, goo*i closure
100
.00031
.031
Total transmittance (T)
0.5695
fore a V 2400
f0r° T ~ I, ~ 0.5695 ~ L
and
10 logio 4210 = 36.2 db
That is, the noise-reduction factor, or the effective insulation which the room provides
against outside noise, is 36.2 db. Thus, if the studio is located where the outside noise is
at a level of 60 db, the level of the noise which reaches the studio will be 60 — 36.2 or
23.8 db. It will be noted that most of the transmitted noise is that which comes through
the glass windows, and that therefore the noise-reduction factor can be increased con-
siderably by means of double windows or by dispensing with the windows.
ACOUSTIC DESIGN OF AUDITORIUMS
By Vent O. Knudsen
31. THE HEARING OF SPEECH IN AUDITORIUMS
Four principal factors affect the hearing of speech in auditoriums: the shape of the room,
the loudness of the speech which reaches the listeners, the reverberation characteristics
of the room, and the amount of noise in the room. If average speech is loud and distinct,
and entirely free from the interfering effects of noise and reverberation, the percentage
articulation for the average listener will be 96, that is, 96 out of 100 meaningless monosyl-
labic speech sounds will be heard correctly.
In an equation for calculating the percentage articulation for a room it will be necessary
to introduce reduction or distortion factors due to (1) the shape of the room, (2) inadequate
loudness, (3) excessive reverberation, and (4) extraneous noise. It is possible to represent
approximately the percentage articulation in any room by the equation
Percentage articulation — QGkJciktk* (1)
where k, — the reduction factor due to the shape of the room.
ki — the reduction factor due to the inadequate loudness of speech.
AT = the reduction factor due to the excess of reverberation in the room.
k^ = the reduction factor due to the extraneous noise in the room.
12-70
ACOUSTICS
In the ideal room each of these factors will be equal to unity, so that the percentage
articulation under such conditions would be 96 per cent.
Experimental data have been obtained by means of which it is possible to determine the
appropriate values of these four factors for any auditorium, although considerable re-
search remains to be done before accurate values of ks are known. When these factors
are determined for a certain auditorium and substituted in eq. (1) the resulting product
gives the probable average percentage articulation in that auditorium.
It is admittedly only an approximation to represent these factors by single numbers.
For example, the reverberation is described not by a single number but by a curve giving
the times of reverberation at different frequencies. However, if one takes the time^ of
reverberation for a tone of 512 cycles, one will have a fairly reliable index for representing
the condition of reverberation in a room, especially if the reverberation time does not vary
too widely at different frequencies. Such a single index is very useful for rating the
acoustical quality of rooms. In problems of design, on the other hand, consideration
should be given to the reverberation throughout the entire range of frequencies. Similarly,
the noise spectrum in the room and the shape of the room cannot be represented rigorously
by single numbers. However, in the rectangular room of conventional shape it is not only
admissible to use a single factor to represent the effect of shape on articulation, but the
factor ka will not deviate appreciably from unity.
The four factors which affect the hearing of speech in rooms will now be considered
separately.
SHAPE. It is not only necessary to avoid shapes which will produce acoustical defects,
such as echoes, flutters, sound foci, interfering effects, and "whispering gallery" effects,
but it is of prime importance to design shapes which will facilitate the most advantageous
flow of sound energy to all auditors in the room.
There axe three outstanding forms which should never be tolerated: (1) those which will
produce a pronounced focusing of sound, thus giving an excessive concentration of sound
in some places and a scarcity of sound in other places; (2) those which will produce exces-
sive delays between the sound which reaches the auditors by a direct path from the source
a-nd that which reaches the auditors by reflection from the ceiling or walls ; and (3) those
in which the sound reaching the auditors
travels a relatively long distance, at
grazing incidence, over a highly absorp-
tive surface. The sound which comes
by the reflected paths always has to
travel a greater distance than that which
comes by the direct path, and if the
difference in these path lengths is as
great as 65 ft the reflected sound will be
delayed to the extent that it is heard as
a separate sound; that is, the delayed
sound produces an echo. Even when
the reflected sound is delayed as much
as 50 ft it unites with the direct sound
sufficiently out of phase to produce a
FIG. 1. Kefleetion of Sound from a. Domed Ceiling
masking or blurring interference. Figure 1 exhibits a characteristic defect which results
from the use of concave surfaces.
Figure 2 shows a longitudinal section of a cut-away model of an auditorium which is
not only free from concentrations, dead spots, and interfering reflections but also is so
shaped as to give a nearly uniform distribution of diffusely reflected sound to all parts of
the auditorium, with a slight preference for the more remote parts.
In many auditoriums, and even in some sound-recording studios, it may be difficult
or even impossible to avoid large and therefore troublesome differences of path between
the direct and reflected sound. In such instances it is advisable to break up the surfaces
producing these delayed reflections by introducing coffers, beams, pilasters, or other irregu-
larities in contour. A number of rooms, highly acclaimed for their good acoustics, have
been designed with walls and ceiling deliberately covered with polycylindrical sound
diffusers. Figure 3 is a typical example. In rooms where public-address systems are
required, the architect will have greater freedom in designing the shape and size of the
room.
Both speech and music rooms should be designed so that the auditors receive a relatively
large amount of sound which travels directly from the source or from reflectors located
sufficiently near the source so that this reflected sound is nearly in phase with the direct
sound. The stage, pulpit, platform, choir loft, or other location for the speaker or per-
former should be well elevated above the audience and provided with large, reflective
1. Acoustically treated projection booth with sound
amplification equipment and controls for sound
monitoring.
2. Ceiling planes reflect sound to all parts of the
auditorium.
3. Three-channel public address system to reproduce
stage sound in "auditory perspective".
4. High-fidelity speakers: bass-compensated dynamic
speaker for low tones; high frequency directional
horns for high tones.
5. Backstage treated with acoustical plaster to reduce
"stage echoes".
6. Acoustic treatment on walls: over-all distribution
in alternate bands of (a) acoustic tile and (6)
hacdwall plaster,
FIG. 2. Cut-away Model of the High School Auditorium for "Whittler, California. (William Harrison,
Architect.)
7. Proscenium splays, horn-like shape of stage opening
projects sound to audience.
8. Upholstered seats: absorption value of each seat
equivalent to that of a person's clothing.
a. Double doors to foyer insulate against external
noises.
10. Slanting rearwalls on main floor and balcony reflect
sound down toward rear seats.
It. Acoustically treated foyer to reduce external noises.
12, Streamlined balcony improves flow of sound to
rear seats.
FIG 3, Polyeylindrical Sound Diffusers in an RCA Disk Recording Studio in New York. (Volkmann.)
12-71
12-72
ACOUSTICS
surfaces located behind, above, and on both sides of the position where the sound °rigmates.
In addition, especially in large rooms, the floor should rise progressively toward the rear
of the room, or the room should be designed with one or more balconies so that all auditors
obtain an abundance of direct or beneficially reflected sound-the path length o .the re-
flected sound should not exceed that of the direct sound by more than 50 ft, and Preferably
less than that, so that the reflected sound will reinforce, and not interfere with, the direct
sound. Long rooms with level
110
lbel
8
tonslty Uvtfl
8 8
Room B T70f x 200' x;
Absorbent Ceiling
Room A 360' x1 560' x 27'
Non-absorbent -Celling
200
floors, with a low platform or no
platform at all, and with a highly
absorptive ceiling, are especially
poor speech rooms, since much
of the sound reaching the auditors
in such rooms travels at near
grazing incidence over the highly
absorptive audience and also along
the absorptive ceiling. (See Fig.
4.) The intensity of free progres-
sive sound waves propagated over
such surfaces has been found to
diminish as the inverse fourth
power of the distance from the
sound source. Properly designed
0 50 100 150
Distance from the Source In Feet
FIG. 4. Variation of Intensity of Sound with Distance from .
Source in Large Rooms with Absorbent and Non-absorbent reflective surfaces, large compared
Ceilings, Showing the Excessive Decrease in Level Which Oc- -+-L +T^ TTTOTrola-no-f-'h r>f +h<* «innnr?
curs When Sound Travels over or along an Absorptive Surface W1jf ltne waveiengi:n 01 une bouna,
will largely compensate for such
excessive losses and will insure adequate loudness of unamplified speech for rooms having
volumes of less than about 50,000 cu ft. For larger rooms it is necessary to amplify the
speech with a suitable public-address system.
For further details regarding shape of rooms consult Bagenal and Wood, Planning for
Good Acoustics; Knudsen and Harris, Acoustical Designing in Architecture; and the current
and bound volumes of the Journal of the Acoustical Society of America.
NOISE. The curve in Fig. 5, obtained empirically, gives the value of the noise-
reduction factor kn for different amounts of noise. The abscissa is the ratio of the sound
level of the noise, in decibels, to that of the speech, also in decibels. Thus, when the noise
1.0
.8
.6
•as
.4
.2 .4 .6 .8
Ratio of Noise to Speech Levels
FIG. 5. Effect of Noise on the Hearing of Speech
1.0
is at the same level as the speech, the abscissa is 1.0. Although the value of kn given in these
curves is only an approximation, based upon a limited number of measurements, experi-
ence has indicated that it is useful in problems of design or correction.
LOUDNESS. The curve of Fig. 3, p. 12-31, gives the percentage articulation for
speech as a function of the sound level of speech, as determined by Fletcher and Steinberg.
Thus, the optimal sound level of speech, in quiet surroundings, is 70 db above threshold,
and for levels below 40 db the articulation drops off rapidly. The loudness reduction
THE HEARING OF SPEECH IN AUDITOBIUMS 12-73
factor ki to be used in eq. (1) is obtained by dividing the percentage articulation by 96.
The curve in Fig. 6 gives the average speech power, in microwatts, of the average speaker
in rooms of different size. By means of this curve, and the amount of absorption in the
100
8
8
354 7Q7 14.14 2330 5660 11J30G 22,600 45,200 Gi
U500 25,000 50,000 100,000200,000 400,000800,0001,600,000 Cn.Ft
Volume
FIG. 6. Average Speech Power of Speakers in Rooms of Different Sizes
room, it is possible to calculate the average sound level of speech for any auditorium, and
then from Fig. 3, p. 12-31, to calculate the appropriate value of ki. In Table 1 are given
values of ki for rooms of different size and different times of reverberation.
Table 1. Values of ki for Use in Eq. (1)
Time of
Volume of Room, cu ft
tion, sec
12,500
25,000
50,000
100,000
200,000
400,000
800,000
1,600,000
0.50
0.96
0.94
0.92
0.90
0.88
0.85
0.81
0.76
0.75
.97
.95
.93
.91
.89
.87
.84
.80
1.00
.97
.96
.94
.92
.90
.88
.86
.82
1.25
.97
.96
.95
.93
.91
.89
.87
.83
1.50
.98
.96
.95
.94
.92
.90
.88
.84
2.00
.98
.97
.96
.95
.93
.91
.89
.86
3.00
.98
.97
.97
.96
.94
.92
.91
.88
4.00
.98
.98
.97
.96
.95
.94
.92
.89
6.00
.99
.98
.98
.97 .96
.95
.93
.91
8.00
.99
,99
.98
.97 1 .96
.95
.94
.92
REVERBERATION. The curve shown in Kg. 7, empirically determined, gives the
value of kr, the reverberation reduction factor, for different times of reverberation at 512
cycles. This curve is based upon the results of speech articulation data obtained in four-
LO
.8
.6
A
.2
0
1
— *=<
"-^
•^
•s,^
^^•v.
^
"•^
U"""""-S— N
.
— —
5 1.0 2.0 3.0 4.0 5.0 6.0 7.0 8.0 9.
Time of Re verfaeratkjn— Seconds
FIG. 7. Effect of Reverberation on Hearing of Speech
teen different auditoriums having times of reverberation varying from less than 1 sec up
to more than 8 sec. It is seen that kr decreases almost uniformly as the time of reverbera-
tion increases from 1 to about 6 sec. The abscissa in this curve gives the reverberation
12-74
ACOUSTICS
time at 512 cycles. In general, the time of reverberation at 128 cycles should be about
25 to 50 per cent longer than it is at 512 cycles, and the reverberation time should remain
approximately constant at frequencies above 512 cycles, increasing slightly for frequencies
above 2048 cycles.
COMBINED EFFECTS OF LOUDNESS AND REVERBERATION. Since the addi-
tion of absorption to a room diminishes the loudness of speech as produced by the average
speaker, it is reasonable to assume that there will be an optimal time of reverberation for
speech rooms. This optimal time will be attained when a further reduction in the reverber- •
ation will concurrently reduce the loudness of speech to the extent that the impairment
produced by the diminished loudness will just compensate for the improvement occasioned
by the reduction of the reverberation. The curves shown in Fig. 8 were calculated by
means of eq. (1), using the appropriate values of the loudness-reduction and reverberation-
reduction factors. These curves give approximately the average percentage articulation
1UU
90
c 80
JO
« 70
Iso
1
& 50
40
30
c
,urve
Cu. Ft.
(a) 25,000.
(6) 100,000.
(c) 400,000.
(d) 800,000.
» 1,600,000.
Volume
Cu. M.
707
2,830
11,300
22,6CO
45,200
(ay—
(vr~
=^
s^
&
t~\s
^
^
^s"
w
^x
^
^
^
%
^§^5»%
^^
^
LO 2.0 3.0 4.0 5.0 6.0 7.0
Time of Reverberation— Seconds
8.0 9.0
FIG. 8.
Percentage Articulation Curves for Rooms of Different Sizes and Different Times of
Reverberation
which will obtain in rooms of different sizes and different times of reverberation, for the
average speaker, without artificial amplification. If an articulation of 75 per cent is re-
garded as the minimal for satisfactory hearing (see also article 29), it is apparent that
the average speaker will not be heard satisfactorily in an auditorium larger than about
1,000,000 cu ft, no matter what condition of reverberation has been provided for the room.
Also, in an auditorium having a volume of 100,000 cu ft the time of reverberation should
not exceed 2.70 sec. The curves in Fig. 8 are based upon the assumption that the noise
level has been reduced to 30 db, an unusually quiet room, and that k, = 1.0. The need
for artificial amplification of speech in large rooms is apparent; amplification should be
provided in all rooms larger than about 50,000 cu ft, and even in smaller rooms when
considerable noise is present.
The curves in Fig. 8 apply to the average speaker. Speakers with weak voices will not
be heard so well, as is indicated by the curves, and speakers with loud voices will be
heard better.
In all the curves in Fig. 8 it will be seen that the articulation is a maximum for a particu-
lar time of reverberation, and that this optimal time of reverberation increases with the
size^of the room, a fact which is well established by experience. Furthermore, the percent-
age'articulation in Fig. 8 is the average value; in general, the articulation diminishes pro-
gressively with the increase of distance from the speaker.
32. MUSIC ROOMS
The reverberatory properties of a room are of even greater significance for music than
they are for speech. The acoustical properties of a music room are no less important than
those of the musical instrument to be played in that room; indeed, the room and instru-
MUSIC EOOMS
12-75
ment together comprise a coupled system, and it is this combined system that the ear or
microphone "hears." The resonant frequencies of a room, considered in article 20, depend
on the dimensions of the room; their intensities and their rates of growth and decay are
largely influenced by the distribution of the absorptive and reflective materials over the
boundaries of the room.
A music room should be so dimensioned, shaped, and treated with absorptive and
reflective materials as to support and enhance the rich quality of the individual tones and
harmonies of music, and
to join together these
separate tones and har-
monies so that they coa-
lesce into a continuously
flowing melody. The
best music rooms, like
the best violins, are those
which are free from
prominent resonances
and which have a rela-
tively uniform steady-
state response through-
out the entire frequency
range. Rooms in which
the ratio of height,
width, and length is
approximately 2:4:5,
and in which furred-out
wood paneling and wood
flooring on wood joists
comprise most of the
interior boundaries, are
found to meet these
conditions and usually are highly acclaimed by both performers and listeners. The use
of non-parallel pairs of opposite walls, of poly cylindrical diffusers of wood veneer,
similar to those illustrated in Fig. 3, and of "patches" of absorptive materials
distributed over walls and ceiling so as to give an ergodic diffusion of sound has given
good results.
The design of music rooms should always be guided by the principles of wave acoustics.
However, the optimal reverberation characteristics can be best calculated by means of
the approximate formulas of geo-
metric acoustics, such as eq. (3)
of article 19.
The optimal reverberation
time for music rooms depends
not only on the size of the room
but also on the type of music to
be performed in the room. The
ideal arrangement should pro-
vide for adjustable reverberation
so that the optimal reverberatory
properties can be readily ob-
tained for all musical perform-
ances for which the room is de-
signed.
The chart in Fig. 9 shows the
optimal times of reverberation
for both speech rooms and music
rooms. This chart applies for
Go. Ft 12,500 25,000 50,000 100,000 200,000 400,000 800,000
Volume of Room
FIG. 9. Optimal Reverberation Times for Speech and Music Booms
3.0
2 0
Music
Speech
\
1.0
0
^
:^
*^n
^^
Speech
Music
64 128 256 512 1024 2048 4096
Frequency-Cycles per Second
FIG. 10. Optimal Reverberation Times at Different Fre-
quencies, for Speech and for Music, When the Optimal
Reverberation Time at 512 Cycles Is 1.3 Seconds.^ Similar
curves should be used when the optimal time at 512 cycles
differs from 1.3 seconds.
a frequency of 512 cycles. As for speech, the reverberation time at 128 cycles should be
approximately 25 to 50 per cent longer than the time for 512 cycles; the reverberation
time should remain approximately constant for frequencies between 512 and 2048 cycles,
and should increase slightly for frequencies above 204S cycles (see Fig. 10).
Experience has shown that the most satisfactory reverberation time for radio
broadcasting or sound-recording studios is about two-thirds to three-fourths of the
accepted time for speech or music rooms (see also Section 16, Sound-reproduction
Systems) .
12-76 ACOUSTICS
33. PRACTICAL PROCEDURE FOR OBTAINING GOOD ACOUSTICS
IN BUILDINGS
The procedure for obtaining good acoustics in buildings begins with the selection of the
site and ends with the furnishing, testing, and maintaining of the building. The necessary
steps, approximately in chronological order, are as follows:
1. Selection of a suitable site (sound studios, theaters, schools, churches, and hospitals,
especially, should be located in quiet surroundings).
2. Noise survey, at the proposed site, to determine the amount of insulation required to
reduce the noise level in the building to a satisfactory point.
3. Insulation against outside noise, which includes not only the selection of the proper
sound-insulative and sound-absorptive constructions but also the proper arrangement of
rooms, corridors, entrances, windows, landscaping, and other appurtenances of the building.
4. Design of the shape of the room (shapes should be designed which not only will avoid
such acoustical defects as echoes, interfering reflections, room nutter, and sound foci, but
also will facilitate the most advantageous flow of diffuse sound energy to all auditors in the
room, and at the same time will preserve or even enhance the natural beauty of speech and
music).
5. Control of the noise within the building, including solid-borne as well as air-borne noise
and vibration.
6. Selection and distribution of the absorptive and reflective materials to provide the optimal
conditions for both steady-state and transient sounds throughout the room, a problem which
deserves special study and careful planning, and one which involves, besides the acoustical
characteristics of the materials, such properties as structural strength, decorative possi-
bilities, adaptability to the surfaces available for, or requiring, absorptive treatment,
maintenance, sanitation, ease of application, fire hazard, absorption of water, attraction
for vermin, "fool-proof ness," durability, and cost.
7. Supervision of the installation of acoustical materials (especially necessary for the
application of acoustical plaster — in large buildings it is advisable to require the plastering
contractor to prepare a small room for test and approval before the plaster is used in
other parts of the building).
8. Installation of high-quality amplifying equipment under the supervision of a competent
engineer is necessary in all large auditoriums; even in rooms seating as few as 200 or 300
persons it will be found that many speakers have weak voices that require amplification.
9. Inspection of the finished building should include tests to determine whether the
sound insulation, the sound absorption, and the other acoustical properties have been
satisfactorily attained.
10. Maintenance instructions, preferably in loriting, should be left with the building man-
ager, indicating (a) how the acoustical materials can or cannot be cleaned or redecorated,
(6) which furnishings in the building are essential to good acoustics, and (c) how the
humidity of large speech and music rooms should be maintained in order to avoid excessive
absorption of high-pitched sounds.
The foregoing steps, or their equivalent, if carefully executed, will lead to good acoustics.
Developments in modern theories of room acoustics, supplemented by additional empirical
data, will contribute to more reliable criteria than are now available for determining the
best acoustical shape of a room and the most favorable distribution of absorptive and re-
flective materials throughout the room; but if proper use is made of what is now known
there need be no anxiety respecting the outcome in the acoustics of buildings — the out-
come will be good.
BIBLIOGRAPHY
Bagenal and Wood, Planning for Good Acoustics. Methuen/ London (1931).
Davis and Kaye, The Acoustics of Buildings. G. Bell and Sons, London (1927).
Fleming and Allen, Modern Theory and Practice in Building Design, The Institution, London (1945).
Fitzmaurice and Allen, Sound Transmission in Buildings, His Majesty's Stationery Office, London
(1939) .
Glover, Practical Acoustics for the Constructor. Chapman and Hall, London (1933). (Contains a
complete bibliography of books and journal articles.)
Knudsen, V. O. Architectural Acoustics. John Wiley (1932),
Knudsen and Harris, Acoustical Designing in Architecture. John Wiley (1949).
Rettinger, Applied Architectural Acoustics, Chemical Publishing Co. (1947).
Sabine, P. E., Acoustics and Architecture. McGraw-Hill (1932).
Strutt, Raumakustik. Handbuch der Bxperimentalphysik, Bank XVII/2. Akad. Verlagsgesellschaft,
Leipzig (1933). *^ '
Watson, F. IL, Acoustics of Building*. John Wiley (193S).
SECTION 13
ELECTROMECHANICAL-ACOUSTIC DEVICES
EFFECTS OF THE ACOUSTIC MEDIUM
BY HUGH S. KNOWLES
ART. PAGE
1. Physical Properties of Common Acoustic
Media 02
2. Mechanical Impedance to Motion of
Some Simple Acoustic Radiators 03
3. Horns 05
LOUDSPEAKERS
AND TELEPHONE RECEIVERS
BY HUGH S. KNOWLES
4. Acoustic Radiators 08
5. Efficiency 10
6. Moving-conductor Speakers 11
7. Magnetic-armature Speakers 15
8. Condenser Speakers 16
9. Pneumatic Speakers 17
10. Telephone Receivers (Earphones) 17
11. Performance and Tests 18
MICROPHONES
BY HUGH S. KNOWLES
12. Force on the Microphone 22
13. Moving-conductor Microphones 23
14. Condenser Microphones 24
15. Magnetic-armature Microphones 25
16. Crystal Microphones 25
17. Carbon Microphones 26
18. Directional Characteristics 26
19. Performance and Tests 26
MAGNETIC RECORDING
AND REPRODUCING OF SOUND
AnT BY L. VIETH and H. A. HBNNING PAGB
20. Erasing, Recording, and Reproducing
Arrangements 28
21. Erasing, Recording, and Reproducing
Processes 29
22. Recording Media 35
MECHANICAL RECORDING
A1*D REPRODUCING OF SOUND
BY L. VIETH and H. A. HENXING
23. Recording Instruments 37
24. Recording and Reproducing Media, 40
25. Reproducing Instruments 43
26. Sources of Distortion 45
PHOTOGRAPHIC SOUND RECORDING
BY C. R. KEITH
27. Light-valve Recording System 48
28. Refiecting-galvanometer Recording Sys-
tem 50
29. Flashing-lamp and Kerr Cell Recording
Systems 51
30. Sound-on-film Reproducing Systems 52
PIEZOELECTRIC CRYSTALS
BY W. P. MASON
31. Definition of Effects 55
32. Application of Piezoelectric Crystals ... 58
33. Properties of Quartz 58
34. Properties of RocheEe Salt 65
35. Properties of Ammonium Dihydrogen
Phosphate (ADP) 68
13-01
ELECTROMECHANICAL-ACOUSTIC DEVICES
EFFECTS OF THE ACOUSTIC MEDIUM
By Hugh S. Knowles
"An electroacoustic transducer is a transducer which is actuated by power from an
electrical system and supplies power to an acoustic system, or vice versa." (I.R.E.
Standards.)
The theory of operation of electroacoustic transducers is an extension of the theory of
electromechanical transducers, in which account is taken of the reaction of the fluid, or
acoustic medium, on the diaphragm. (See Section 5, article 33.)
1. PHYSICAL PROPERTIES OF COMMON ACOUSTIC MEDIA
The velocity of a sound of small (infinitesimal) wave amplitude depends on the elas-
ticity and density of the fluid. The velocity of propagation, c, of a sound wave is
cm sec-* (1)
where k is the volume modulus of elasticity, p is the density in grams cm~3, 7 is the ratio
of the specific heat at constant pressure to that at constant volume, and PQ is the static
pressure of the fluid.
The characteristic impedance, ZQ (also sometimes called surge impedance or acoustic
resistance) , of the medium is
ZQ =* V&p = pc mechanical ohms em~2 (2)
1. Air. The density, p, at 20 deg cent and po = 760 mm ( = 10s dynes cm"2) is 0.001205
gram cm""3; y == 1.41, giving
c = 33,060 -h 610 cm sec"1 (3)
where 6 is the temperature in degrees centigrade. Also the radiation resistance of air is
ZQ = 42.8 — 0.0790 — 41.2 mechanical ohms cm^2 at 20 deg C (4)
The pressure level, Lp, in decibels is
LP - 20 logic - = 74 + 20 logioj> (5)
Po
where p is the pressure and pp the reference pressure of 0.0002 dyne cm"2. The intensity, I,
in the direction of propagation, of a plane or spherical "free" (i.e., no reflections) sound
wave is
_2
/ = ^- = 2.42 X 10 "V watt cm-2 (6)
PC
where p is the rms sound pressure in dynes cm"2.
2. Hydrogen. The density, p, of hydrogen at 0 deg cent and at po = 760 mm is approxi-
mately 0.00009 gram cm~3. The velocity c = 1.26 X 106 cm sec"1, from which ZQ = 11
mechanical ohms cm~2.
3. Water. The density, p, of water is = 1.0 gram cm""3. The value of c at 20 deg cent
= 1.46 X 105 cm sec"1, from which ZQ — 1.46 X 105 mechanical ohms cm"2.
REACTION OF ACOUSTIC MEDIUM ON A DIAPHRAGM. The audible frequency
range of sounds ©overs roughly 10 octaves. Even the more important range from 80 to
8000 cycles covers nearly 7 octaves, giving a wavelength range of roughly 428 cm (14.1 ft)
to 4.28 cm (1.69 in.). Radiation, diffraction, and reflection phenomena which depend on
the relative length of the sound wave and the linear dimensions of the radiator, or collector,
therefore differ greatly in different portions of the wavelength range, and hence simplifying
assumptions can ordinarily be made only over restricted frequency ranges.
13-02
MECHANICAL IMPEDANCE TO MOTION
13-03
2. MECHANICAL IMPEDANCE TO MOTION OF SOME
SIMPLE ACOUSTIC RADIATORS
The impedance to motion of a diaphragm is altered by its contact with the acoustic
.
SOURCE RADIATING PLANE SOUND WAVES. The impedance per unit area in
contact with the fluid is the characteristic impedance of the medium, and the total increase
in mechanical impedance to motion of a radiator of effective area, S, resulting from contact
with the fluid medium, is »
*/ - rf = *bS (7)
or = 41.2 X S mechanical ohms hi the case of ah*. At any frequency, the radiated acoustic
power is
Pt = 3VO-' (S)
or 4.12 X 10 -6s2 X watts in the case of air (s is the velocity of the radiator element).
PULSATING SPHERE RADIATING SPHERICAL SOUND WAVES INTO AN
UNLIMITED ACOUSTIC MEDIUM. A pulsating sphere is one in which the surface
vibrates or pulsates with small amplitude and uniform velocity in a radial direction. At
any frequency the impedance per unit area in mechanical ohms is
ZA' = TA' + j%
pc
pR
(9)
where k = 2?r/X = w/c = 2-n-f/c, where X is the length of the emitted sound wave, and R
is the radius of the sphere in centimeters. This leads to an equivalent circuit of parallel
mass and resistance elements of values (for the whole surface) m/ — 4xpfi3 grams and
Tf = 4.7rR2pc mechanical ohms.
Graphical plots of TA' and XA' are given in Fig. 1. The imaginary or reactance term is
in phase with the acceleration and is an inertia or mass reactance term.
so
1
~\
50
40
30
|§2°
'o >- 8
^
s~+*
S
[7^
'
/
f
\
\
N
mpedance per Sq Cm
per Sq Cm per Cm p
co M to w £kuicn
-jAt-
-*
i
/ \
'i
•^
*j
r
)
\J
k
^^
/
/
f
1
x>
\f\^
V
y
^
'/
\
\
0) 03 .6
=f i
Is i
.2
.0
^jX-
\
//
1
/
y
^
.'
1
^
^
/
1 1
/
Dl .002 ,004 .01 .02 .04 .08.1 .2 ,3.4 .6.81.0 2 3 4 6 S 10 2030 60 10
KR=1^=«S.
FIG. 1. Air Resistance and Reactance per Unit Area on One Side of a Pulsating Sphere of Radius
R(T'A and X'A) aad on One Side of a Circular Piston of Radius R (r A and XA) in an Infinite Baffle
The fluid increases the impedance to motion of the spherical surface or diaphragm by an
amount z/ = SZA'. At any frequency the radiated acoustic power is Pf = IV/ X 10 ~7 watt.
Special Case of a "Point** Source (R = 0). When the length of the sound wave is
large in comparison with the radius of the sphere (\^> R and
= lirpR* —
mechanical ohms
(10)
13-04 ELECTKOMECHANICAL-ACOUSTIC DEVICES
CIRCULAR RIGID DIAPHRAGM OR "PISTON" reciprocating or vibrating sinus-
oidally in a (perfect-fitting) cylindrical hole, in an infinite P^?7^f °f^™%^ra^*^5
into an unlimited fluid (' 'semi-infinite" medium) on each side of the baffle, is another
configuration of interest. (R is the radius in centimeters.)
The impedance per unit area is not constant over the surface in this case, but since the
radiator is assumed rigid an average value may be taken. At any frequency the impedance
in mechanical ohms cm"2 is given by ZA = rA + jxA as plotted in .big. 1.
Since the imaginary term is in phase with the acceleration, it is a mass reactance term.
The increase in mechanical impedance to motion of a piston, z/ = rf + yxf - £>(fA -rJXA),
which results from an air "load" may be obtained directly fromthese curves by multiply-
ing the ordinate for any value of kR by the area of the piston When the fluid is air, piston
radiators are usually operated with fluid on both sides of the baffle. Both sides of the
piston must then be considered, in which case S - 2ir#. The total apparent increase in
mass of the piston is mf = SXA/M- At any frequency, the radiated acoustic power is
P/Special Case ofT^Point" Source (R - 0). When the length of the sound wave is
large in comparison with the radius of the piston, the impedance per unit area is
. ju pR (11)
Frequency, CPS for 12 Speaker (10^ Piston)
5O 60 70 80 100
300 400
\
\\
Reference to Pig. 1 will show that, for small values of kR, xA^>rA, so that ZA = JXA.
That is the increase in impedance to motion of the piston, which results from contact
with the fluid, is largely reactive. At this low-frequency condition the radiation imped-
ance of the piston may be represented by an equivalent circuit of parallel mass and resist-
ance elements of values 8pfi»/3 grams and (128/9^) wR*pc mechanical ohms respectively.
The values are O.OOCSed3 grams and SOld2 mechanical ohms, d being the piston diameter
in niches. . . ...
It has been found experimentally that when a conventional rigid conical diaphragm
loudspeaker is used S is approximately the area of the "base," or large end, of the cone;
also, that the usual magnetic
structure changes the radiation
from the rear surface of the
cone by a negligible amount at
low frequencies.
MULTIPLE PISTON'S.
When more than one piston
radiates into a common region
in the medium any one position
experiences not only the force
on its surface arising from its
own vibration but additional
forces due to the vibration of
the other pistons. The result-
ant force is the vector sum of
the individual forces. The mag-
nitude and phase of each force
depend on the diameter, veloc-
ity, and frequency of vibration
of the piston giving rise to the
force and upon its distance from
the reference piston. The ratio
of the resultant force on any
piston, to its velocity, is the
PIG. 2. Ratio of Total Radiation Resistance of a Piston, Vibrat- total fluid or radiation imped-
KpS^e^elSe%^nR^^effSATfto ««* ""A comprises the self-
tangent pistons. Curve 3, each of four tangent pistons in square impedance due to its own vi-
array. Curve 4, each outer, and Curve 5, each inner, piston of
four tangent pistons in a straight line. Curve 6, each of two pis-
tons with centers three diameters apart. All pistons have equal
velocities (both magnitude and phase) and equal diameters, and
vibrate in an infinite plane baffle.
= 2
01
0.1
1
\
0.15 0.2
0.3 o.4
2TR _ CJR
X c
0.5 0.60.70.8 i.o
bration, discussed above, and
the mutual impedances due to
the vibration of the other pis-
tons. From Fig. 2 it will be
seen that the real part of the
total impedance increases as the distance between the pistons decreases and their num-
ber and hence total area increase. When the pistons are close together, vibrate with
equal amplitude, and are separated by a small fraction of a wavelength, they approximate
a single piston equal in area to the combined area of the individual pistons. It may also
HORNS
13-05
be seen that as the separation and frequency are increased the phase of the force arising
from the vibration of the other piston is retarded and may give rise to a component out of
phase with the velocity of the reference piston which lowers the radiation or fluid resistance
below the value the reference piston would have alone. This occurs in curve 6, Fig. 2,
for values of &R/c greater than 0.5.
ENCLOSED BACK PISTON. Same as preceding case but with small enclosure to
suppress radiation from one side of a diaphragm, or to add stiffness to the vibrating
system.
The fluid impedance at the external surface corresponds to the preceding case (note
that S = -n-R*).
If the dimensions of the enclosure are larger than the diameter of the piston the en-
closure adds approximately the same effective mass per unit area, mj, as the unlimited
fluid medium. Therefore, the effective area used in calculating the total effective fluid
mass is S = 2?r.R2, that is, m/ = 2TrJ&m& .
If the length of the radiated sound wave is roughly four or more times the maximum
linear dimension of the enclosure, uniform adiabatic compression of the fluid occurs. The
enclosure then increases the stiffness (see Section 5, article 33) per unit area of the mechan-
ical system by an amount
= -=- cm dyne"1 cm"2
y o
(12)
(Vo is the volume of the enclosure). The total increase in stiffness, s/, due to the fluid,
is SSA.
The enclosure does not approximate a constant stiffness when the length of the sound
wave is less than four times the maximum linear dimension of the enclosure.
If the purpose of the enclosure is to provide a "sink" to absorb back side radiation, ab-
sorbing material is usually placed hi the enclosure. This increases the effective resistance
of the vibrating system. The absorption coefficient of the material used is normally high
enough at the high resonant frequencies of the enclosure to make the enclosure approxi-
mate a semi-infinite medium.
3. HORNS
"A horn is an acoustic transducer consisting of a tube of varying sectional area."
The proper use of a horn, as the radiating portion of a loudspeaker leads to better control
of the response, efficiency, and directional characteristics. In addition these character-
istics may be controlled almost independently of one another.
The total radiation response of a horn considered as an acoustical circuit element is
determined largely by its throat impedance as a function of frequency. In a! well-
designed horns, transmission losses are
ininimized, so that the energy output is Diameter d
closely equal to the input.
The rigorous calculation of the throat
impedance is possible for but very few
useful horn contours, and so approxi-
mate methods are used. The low-fre-
quency region is of greatest interest to
the horn designer, as all horns have a
high-frequency throat mechanical im-
pedance which approaches a constant
resistance that is the same (per unit
area) for all horns. Experiment reveals
that the low-frequency wave fronts in
the horn are smoothly curved surfaces
(Fig. 3) ; by expressing this mathemati-
cally there results a pressure wave equa-
FIG. 3. Low-frequency Wave Fronts in Long Straight
Axis Horn of Circular Croes-sectim
tion in which the only space variable is the axial distance. For convenience, all horn-
design work is usually referred to a straight axis horn of circular cross-section, as in Fig. 3.
The question arises as to what types of horns have this kind of simplified behavior.
Starting from the experimental data it is observed that the "chords" (the diameter, d,
in Fig. 3) for the wave fronts are approximately proportional to the square root of the
area of the wave front, provided that the expansion of the horn is not too rapid. If the
sound pressure is assumed to decrease steadily as the horn expands, modified by the
change of phase down the horn, this assumption may be expressed analytically and in-
serted into the pressure wave equation together with the relation between d and the area
13-06 ELECTROMECHANICAL-ACOUSTIC DEVICES
7=0
of wave front. This leads to a relation between d and x, the axial distance, which when
solved yields
d = dt[cosh (X/XQ) + Tsinh (x/xo)] (13)
Here dt is the diameter at the throat; x0 is a reference distance fixing the rate of taper of
the horn, and is related to the cutoff fre-
quency fe by fe = c/2ira:o; and T is a param-
eter by which a particular] horn contour is
selected. The names "catenoidal horns"
and "Salmon horns" have been suggested
for this family, the latter after the person
who first described their characteristics.
The family is the most general one con-
sistent with the simplifying assumptions
made; f or T = 1 there results the familiar
exponential horn d = dt exp (re/rco), while
for T - oo there results, by a limiting
_ process, the conical horn. At T = 0,
,0, d = dt cosh (X/XQ), which may be termed
the cosh horn. Since this family includes
the most widely used horn contours, it will
be taken as a basis of discussion. Contours for T = 0, 1, 5, and °o are shown in Fig. 4.
The low-frequency throat impedance of all practical horns shows considerable variation
with frequency due to reflections from the mouth. Hence it is common engineering
practice to state as the throat imped-
2.0 , — , _ , - — i - 1 ance that for the infinite horn (outgoing
wave only); in practice the actual im-
pedance varies about the infinite horn
value as a mean, or trend, which is ap-
proached as reflections from the mouth
are decreased. When the mechanical
throat impedance is evaluated for the
horns of eq. (13) there results
Zt = Tt
: Stpc
FIG. 4. Contours of Horns of Eq. (13) for T ••
1, 5, and to
([i- Qfc/OT
1 i - d -
, .
(a) Throat Resistance
0.2
(14)
where St is the throat area; pc is the
characteristic impedance of the me-
dium; the cutoff frequency /« = C/ZTTXQ,
c being the velocity of a free sound
wave. An examination of eq. (14) re-
veals that rt is zero for f < fe (for the
infinite horn) , so that below fc the im-
pedance is entirely reactive. Figure 5
shows rt/Stpc and xt/Stpc as functions
of f/fc for T = 0, 0.5, 1, and 5. The
equivalent circuit of the mechanical im-
pedance of eq. (14) is as shown in
Fig. 6; note that the parallel elements
are simple; only m* varies with Z7, and
only rt varies with /.
f/fc
10
Throat Reactance
FIG. 5. Throat Impedance of Infinite Horns of Eq.
(13). The fc in the abscissa is the cut-off frequency.
FIG. 6. Equivalent Circuit of Throat of
Horns of Eq. (13) . Negligible reflection from
mouth.
The selection of the optimum member of the above family of horns cannot be considered
apart from the loudspeaker unit or other source out of which the horn is to work, as both
HORNS
13-07
form a fairly tightly coupled system. The essential mechanical elements are shown in
Fig. 7 for a moving-coil driving unit as discussed in article 6.
The electrical system consists of a generator of constant emf , e, and total electrical
impedance, r«, which is here assumed resistive and equal to the generator resistance proper
plus the blocked resistance of the voice coil. The resulting force input to the circuit of
Fig. 7 is thus $le/ret which is fairly constant for horn loudspeakers. As seen from the me-
chanical mesh, the electrical side also contributes a "source impedance" n = (£kVr. which
is as constant as the force. In
these expressions /S is the mag- /22z2
netic flux density in the gap
and I is the conductor length.
In the purely mechanical sys-
tem mi is the mass of the loud-
speaker motor, and si its stiff-
ness, which may include air
trapped back of the diaphragm.
The stiffness of the air sz, of
volume V, between diaphragm
and horn throat (the sound
chamber), is equal to pc?S<?/V
I — VW O^MJLy — {(•
O *i 7ft S
Force=s
f
FIG. 7. AI.
speaker. (,
te Equivalent Circuit of Typical Horn Loud-
is the impedance ratio of the fluid trans-
former formed by the areas 84 and St.
when referred to the diaphragm area Sd- Because Sd is usually different from Si the horn
throat elements of Fig. 6 appear at the diaphragm multiplied by the fluid transformer
impedance ratio (Sd/St)z, which is controlled by the horn.
The configuration of the circuit is that of a band-pass filter; however, this is not a satis-
factory basis of design, as only a half section is present. In practice a fiat response is not
always the desired goal, and so the elements are chosen with a particular application in
mind. Usually the unloaded resonant frequency, f\ — — ( — J , of the motor is placed
2v \mi/
below the midband, while the other resonant frequency, fz — — ( — j , is placed above.
The bandwidth is fixed largely by ss/Sj; thus the sound-chamber volume and hence the
clearance to the diaphragm should be as small as possible for a wide band. The horn
influences this by controlling m% through the parameter T, permitting /j to be properly
placed, with a suitable $2.
The sound chamber, which may be regarded as a part of the horn just as a transformer
is often associated with a loudspeaker, serves to reduce the effect of mi at high frequencies
by the mi — Sa resonance. Simi-
larly at low frequencies the m±— si
resonance, as influenced by the
value of T, may produce a rise in
response. This reactance annul-
ling permits good low-frequency
response to be obtained by plac-
ing the horn cutoff frequency, /c,
below /i, the resonant frequency
of the Wi — si combination.
The termination r2 is usually
close to n to obtain approximate
matching in the midHresponse
region, thus governing the maxi-
mum efficiency. This involves
the proper relation between horn-
throat area and useful magnetic
energy in the air gap. When
n == r>, variations in horn-throat
FIG. 8. Approximate Relation between Effective Mouth Di- Smrx^nnnp. Art* to month rofieo-
ameter and Frequency for Exponential Horn impedance due to moutft rejec-
tions have a minimum enect on
the radiated power. These reflections are minimised also when the product of mouth
diameter in inches and cutoff frequency in cps is greater than 4000; this product may be
made as little as 2000 if r2 = n-
Since diaphragms are often called on to radiate energy at wavelengths for which destruc-
tive interference may take place across the diaphragm, it is usual to remove the radiation
by one or more annular slots so placed that phase effects are minimized. The annular
passages may then be constricted in average diameter until the circular horn section is
reached.
0.1
10*
2 x 104
fd,
5xl04 105
, in CPS x Inches
2xl05
13-08 ELECTROMECHANICAL-ACOUSTIC DEVICES
The directional properties of a horn are largely determined by the ^ mouth geometry,
particularly the diameter and slope. As frequency is increased, there fe reached a value
at which the emergent sound is so directional that the wave does not "touch" the mouth
portion at all. Thus the effective mouth diameter decreases as the frequency is raised,
and in some designs the polar response pattern becomes almost independent of frequency.
Data reported in the literature may be presented in the form of equivalent mouth diameter
as a function of frequency. In Fig. 8 this is shown for one group of measurements on
exponential horns; the curves are rough approximations and should be taken as indicating
only the trends. The ratio (dem/dm) is that of equivalent and actual mouth diameters.
In general, the steeper the mouth slope, the less directional the horn; but, if this, generali-
zation is carried too far, the violence done to the wave fronts appears as a rough response
characteristic. The directional effect of horns is not too serious hi practical applications,
for often this property is useful in reducing acoustic feedback and improving the sound
level in a desired localized region. When uniform radiation over a large solid angle is re-
quired, multicell horns are commonly used. Often the shape of the horn may be altered
so as to provide improved distribution, and this frequently results in a more uniform space-
response variation.
BIBLIOGRAPHY
American Standard Z24.1-1942. (Terminology.)
BaUantine, Stuart, J. Franklin Inst., VoL 203, 86 (1927). (Bessel horns.)
Crandall, I. B., Theory of Vibrating Systems and Sound, p. 85 ff. (Impedance of medium and of horns.)
Hall, W. MM J.A.S.A., Vol. 3, 552 (1932). (Sound field in horns.)
Hanna, C. R.t and J. Slepian, Trans. AJ.E.E.t Vol. 43, 393 (1924). (Horn loudspeakers.)
Hoersch, V. A.t Phys. Rev.t VoL 25, 218 and 225 (1925). (Transverse vibrations in horns.)
International Critical Tables, Vol. 4, 453 (1929). (Constants.)
I.R.E. Standards on Electroacoustics (1938). (Terminology.)
Klapman, S. J., J.A.S.A., Vol. 11, 289 (1940). (Multiple pistons.)
Lamb, BL, Proc. Roy. Soc. London, VoL 98, 205 (1920). (Fluid impedance.)
McLachlan, N. W., Loudspeakers (1934). (Fluid impedance, general, and bibliography.)
McLachlan, N. W., and S. Goldstein, J.A.S.A., VoL 6, 275 (1935). (Finite pressure distortion horns.)
Mason, W. P., B.S.T.J., VoL 6t 258 (1927). (Horns and other acoustic elements.)
Phelps, W. D., J.A.S.A., VoL 12, 68 (1940). (Finite horn boundary impedance.)
Eayleigh, J. W. S.» Theory of Sound, VoL II, 164. (Fluid impedance.)
Salmon, V., J.A.S.A., VoL 17, 199 and 212 (1946). (Horns.)
Stewart, G. W.f and Lindsay, R. B., Acoustics, p. 132. (Horns and general.)
Thuras, A. L., R. T. Jenkins, and H. T. O'Neil, B.S.T.J., VoL 14, 159 (1935). (Finite pressure
distortion horns.)
Van Urk, T., and R. Venneulen, Philips Tech. Rev., VoL 4, 213 (1939). (Radiation admittance.)
Webster, A. G., Proc. Nail. Acad. Sci., VoL 5, 275 (1919). (Horns.)
LOUDSPEAKERS AND TELEPHONE RECEIVERS
By Hugh S. Knowles
A loudspeaker is an electroacoustic transducer actuated by energy from an electrical
system and radiating energy into an acoustical system, the spectral composition of the
energy in the two systems being substantially equivalent. Loudspeakers may be classified
as to type of radiator or radiating system, type of motor, and reversibility.
4. ACOUSTIC RADIATORS
DIAPHRAGMS. The transformation of electrical into acoustical energy is usually
accomplished by electrically actuating a surface or diaphragm in contact with air, or some
other fluid, causing it to move and set the adjacent ah* particles in motion. (See, however,
article 9.) When the resulting radiation is into a large solid angle the radiation resistance,
or real part of the fluid impedance, is low when the length of the radiated wave substan-
tially exceeds the diameter of the radiator. The diaphragm serves to couple the air, which
has low impedance per unit area, to a motor having a relatively high mechanical impedance,
•when connected to its source of electrical energy, viewed from the diaphragm.
The low radiation resistance is unfortunate both because of the problem of obtaining
efficient energy transfer and because large diaphragm amplitudes are required to radiate
appreciable power at low frequencies. Figure 1 shows the peak diaphragm amplitude, or
half the total diaphragm displacement, required of several piston sizes to radiate 1 watt.
One-tenth this amplitude is required to radiate 10 milliwatts. These curves cover the
frequency range in which the radiation resistance is proportional to the square of the fre-
quency and to the fourth power of the piston radius.
ACOUSTIC RADIATORS
13-09
Most diaphragms are conical in shape and, if rigid, displace the same amount of air for
the same amplitude as would a fiat piston having a diameter equal to the diameter of the
base of the cone. At low frequencies the base diameter of the cone is therefore taken
as the equivalent piston diameter.
The size of the usual conical diaphragm, frequently called a cone, is limited by the need
for increasing its mass per unit area as the area is increased in order to maintain adequate
stiffness. It is customary to make the diaphragm thickness vary almost directly with the
diaphragm diameter. This largely offsets the improved resistance-reactance ratio of the
fluid impedance.
The conical diaphragm may be thought of as a conical transmission surface in which
there are both radial and circumferential waves. At low frequencies only the radial wave
need be considered. The flexible
annular support or "surround" pro-
vides a termination for the base or
large diameter of the conical surface.
The flexural phase velocity of the
radial wave in the diaphragm and
the impedance of the termination
are such that the effective length is
one-quarter wave at 600 to 1000 cps
in large diaphragms (16-in. to 10-in.
"pistons") and at 1000 to 2000 cps
in small diaphragms (8-in. to 2-in,
"pistons"). Below this frequency
all parts of the cone move in phase
although the amplitude is not sub-
stantially uniform except at lower
frequencies where the radial length
is a small fraction of a wavelength.
If the annular support behaves as a
non-linear stiffness over the required
amplitude range, as it frequently
does, the diaphragm may flex in a
complicated way even at low fre-
quencies.
Wave transmission in the dia-
phragm is desirable because it results
in a more favorable high-frequency
driving point impedance into which
the motor is coupled. It also results
.01
40
60 SO IOQ 20O
Frequency in CPS
40O 600 10OO
PIG. 1. Displacement of Piston from Equilibrium Position
Required to Radiate 1 Watt. The total displacement is
twice the value given. (If both sides radiate, divide by
in a broader high-frequency direc-
tional pattern than would obtain if the diaphragm were a rigid piston. When maximum
loudness is required, a diaphragm made of materials having low internal dissipation such
as pressed or calendered paper and a low-resistance flexible annular termination is used.
When a smoother response-frequency curve is desired with reduced transient distortion
and the reduced loudness can be tolerated, a "soft" more blotterlike material with higher
fiexural resistance is employed, sometimes with a dissipative termination of leather, felt,
cloth, or a dissipative elastomer. The modes of vibration of the diaphragm are also in-
fluenced by cone angle, lumped masses and compliances (usually annular beads or corruga-
tions), impregnants, etc. Because of the complex behavior of diaphragms most design
work is largely empirical.
To reduce the mass per unit area and yet obtain the benefit of a large radiating area
multiple diaphragms are frequently used. If all the diaphragms vibrate in phase and with
the same amplitude the average radiation impedance seen by the array will correspond
to that of a single diaphragm of equal area. (See p. 5-66.) By properly orienting the
speakers the spatial radiation pattern, at high frequencies, may be improved.
In addition to the common right circular cone shape two others are sometimes used.
The conoidal or "curvilinear" is used when an increase in radiation above 5000 cps is
wanted at the expense of the 2000-5000 cycle region. The elliptical shape is sometimes
used when space requirements limit one dimension of the cone. Unfortunately the limited
dimension is usually the vertical one, resulting in the major or long axis of the ellipse being
mounted horizontally. Contrary to popular belief this leads to a narrow horizontal and
wide vertical high-frequency directional pattern as predicted from theoretical considera-
tions. In spite of the appeal of its shape the oval or elliptical diaphragm has had limited
acceptance because it is more difficult to fabricate, its response is more difficult to adjust,
13-10 ELECTROMECHANICAL-ACOUSTIC DEVICES
it has less radiation resistance in the middle-frequency range than a circular diaphragm
of identical area, and its asymmetrical support leads to cone and moving-coil distortion
which necessitate larger air-gap clearances for a comparable safety factor.
Over the frequency range in" which the fluid mass, m/, is substantially constant most
conical diaphragms behave as a rigid piston of mass mm. If the flexible centering members
supporting each end of a conical diaphragm are linear (displacement proportional to force) ,
their stiffnesses may be combined into an equivalent stiffness sm or equivalent com-
pliance Cm.
HORNS. The radiation from a horn may be considered as originating at the mouth,
with the remainder of the horn serving to "match" the mouth and throat terminating
impedances. Tor this purpose it is important that the walls be relatively non-porous and
non-vibratile.
The theory has been developed on the basis of a straight axis horn of circular crps*-
section, with no reflections from the mouth. One common departure from these idealized
conditions is in the shape of the axis. It may be bent, as in the low-frequency horns used
in theater systems, or it may be folded, as in re-entrant public-address horns. The contour
of the boundary at the changes in the direction of the axis must usually be selected em-
pirically because of the complex manner in which the wave front executes the change in
direction. The contour must also be selected so as to avoid exciting transverse modes of
vibration of the air. This requires smoothly and symmetrically changing contours, and
careful attention to the symmetry of the driving diaphragms with respect to the throat
of the horn.
In practice, the cross-sectional area may be circular, rectangular, or annular, the last
two corresponding to the theater and public-address horns mentioned above. In these
horns the lateral dimensions are chosen to retain the same area-axial distance relation as
in the circular (reference) horn.
The effect of mouth reflections may be minimized by proper attention to the horn
driver unit (see article 3) . Advantage may be taken of reflections to load the horn unit
at frequencies near cutoff for which the radiation resistance is normally low.
5. EFFICIENCY
The total power dissipated by the mechanical system is
Pmf = S*Tmf - &(Tm + r,) - — f- (Tm + Tf) (1)
in which rm and r/ are the mechanical and fluid resistances, / is the current in the electric
mesh and 2*2 is the total self-impedance of the mechanical system, and the electrical and
mechanical meshes are numbered 1 and 2 respectively. (See Section 5, article 33 and
eqs. [4a] to 5J>] below.) -
Energy Efficiency. The ratio of acoustic power (or energy) output to electric power (or
energy) input is called the energy or conversion efficiency and corresponds to the definition
of efficiency commonly used for most transducers other than electroacoustic ones. This
efficiency is
where rmc is the blocked resistance of the system.
System Efficiency. Because both the modulus and phase angle of the normal input
impedance of the speaker vary with frequency, the speaker in general absorbs less power
from the source than an ideal load or transducer would. Since this inability of the trans-
ducer to absorb maximum power limits the useful power output of the source, it in effect
reduces the "efficiency" of the transducer.
To take this property into account, the ratio of the acoustic power output to the electric
power input which the source would supply if connected to an ideal transducer is defined
as the system or absolute efficiency. If the source is a vacuum tube or generator whose
internal impedance is a "pure resistance, Tg, it supplies maximum power to a resistance of
equal value, and the system efficiency is
•*+*ffiw (3)
where ZM — zi2*/z&, the other quantities are as defined above, and the vertical lines indicate
that the absolute value is to be taken.
MOVING-CONDUCTOR SPEAKERS
13-11
6. MOVING-CONDUCTOR SPEAKERS
"A magnetic speaker is a loud speaker in which the mechanical forces result from mag-
netic reactions."
"A moving-conductor speaker is a magnetic speaker in which the mechanical forces result
from magnetic reactions between the field of the moving conductor and the steady applied
field. (This is sometimes called a dynamic speaker.) IT This classification includes moving-
coil or electrodynamic (sometimes called "dynamic") and ribbon or "band" speakers.
Cross-sections of two typical mov-
ing-coil speakers are shown in Fig. 2. raffle Gasket
The mechanical circuit may be L_jAnnuiu«__ jCone T0ust Cap
considered a series circuit with the
elements m™/, Cm/, and rm/, which
include the fluid impedance. In gen-
eral the circuit elements are func-
tions of frequency.
The actuating force on the con-
ductor is jSK dynes, where & is the
flux density in gausses, I the con-
ductor length in centimeters, and i
the instantaneous current in ab-
amperes (amperes X 10). If the
electrical circuit, including the mov-
ing coil and generator, has a total
series inductance Le, capacitance C«,
and resistance re, and the generator
an instantaneous open-circuit volt-
age e, the instantaneous "force"
equations are
Cone Housing
Field Coil Case
Field Coll
•Pole Piece
+ req + 77 4-
v-<«
(4a)
7r--#$ = 0 (46)
Piece
(6)
FIG. 2. Moving-coil Speakers, (a) Direct radiator type;
(6) horn type.
-Magnet 1— Pole Piece i— Wool Filling
The further assumption is made in
these equations that (3 is a constant,
independent of s, that q does not
alter the magnetic field, and that
there is negligible mutual impedance between the moving coil and the "field" coil which
provides the static field. If j3 is supplied by a permanent magnet, a constant fiux source is
approximated which is little altered by q. The performance of moving-coil speakers de-
pends on j8 and not on whether this is supplied by a permanent magnet or an electromagnet.
If e = E sin coi, the steady-state solution of eqs. (4) is
E = 2l2s -4- Ziil
(So)
0 = 222S — Zi$I (56)
where E, I, and s are the rms steady-state voltage, current, and velocity, and z& = fit is
the force factor. "The force factor of an electroacoustic transducer is a measure of the
coupling between its electrical and mechanical systems. It is the ratio of the open-circuit
force or voltage in the secondary system to the current or velocity in the primary system."
Equations (5) give
-i (65)
f
DIRECT RADIATOR OR HORNLESS SPEAKER. These are the commonly used
electrodynamic speakers which are designed to radiate as efficiently as possible into a solid
angle of the order of 27r(' 'semi-infinite medium"). They are used in baffles or cabinets
when response at low frequencies is required but space limitations prevent the use of a
horn or "directional bafHe" to improve the etficiency. The radiated sound energy is
s2?-/, where s is given in eq. (65) and r/ is SrA, with r± from Fig. 1, p. 13-03, provided the
13-12
ELECTROMECHANICAL-ACOUSTIC DEVICES
mounting approximates an infinite baffle at the frequency considered. In the low and
low middle frequencies, the fluid resistance is proportional to the square of the frequency.
Therefore, if SV/ is to be approximately constant, the velocity s must vary inversely with
frequency. From eq. (66) it may be seen that, when the applied frequency is appreciably
higher than the resonant frequency of the mechanical system, s is largely a function of «12
and 222- Since 212 is approximately a constant, and 222 == &#»»»/, * varies inversely with w
particularly if 212 is small. The radiated acoustic power is therefore approximately in-
dependent of frequency. In this frequency range the system efficiency, r)8, is approximately
2 X
(7)
where a. is the ratio of actual conductor volume to air-gap volume, V (product of gap
length, mean perimeter, and coil winding length) ;
E = — — == gap energy (ergs)
07T
B is the average flux density in volume V (gauss) ; C is the conductivity of the conductor
with respect to copper; m is the effective motor mass (voice coil, cone, fluid mass) (gram) ;
and d is the effective piston diameter (inches) .
When the velocity of the diaphragm is largely limited by the mass reactance of the
mechanical system and varies (roughly) inversely with frequency, the device is said to
have ''inertia control." To obtain uniform response, the natural frequency is placed near
the lowest frequency to be transmitted. In 12-in. speakers this resonant frequency is of
the order of 75 cps. At very low frequencies, either the stiffness reactance or the mechan-
ical resistance limits the velocity, and the response decreases even if the speaker is operated
in an infinite bafiie. In the middle frequency range, the normal impedance and, therefore,
the force on the mechanical circuit are fairly constant. In general the damping is less
than "critical" or the value required to give the shortest transient response. See "Tran-
sient Response," Section 5, articles 13 and 15.
Figure 3 indicates the result of varying /3Z (or 212) on the pressure measured in the sound
field. Since the speaker directivity is almost independent of frequency in this range, the
ordinates are proportional to the total radiated acoustic power. These curves show that
~s
JO.
:^r
"^
£
Q 10
v"
"N.^
v/
^
V
-»^.
12000
S
/.
//
-•x
X**r
v
•.
u 8500
0.
$
^
^
\
\
•'-.
...
6000
5
--?<]
* /
>-
->-,
"•^.
4250
"«
"•*".•**
/
C£
Of)
/
/
40
50
60 70 80 90 100
Frequency in Cycles per Second
150
FIG. 3. Variation in Acoustic Pressure with Flux Density, or Force Factor. (Measurements were
made on the axis, 10 feet from a direct radiator moving conductor speaker.)
speakers having large force factors or values of 212 and high efficiency in the middle fre-
quency range have relatively less response near the resonant frequency of the mechanical
circuit. Increasing the flux density and force factor increases the energy efficiency but
decreases the system efficiency near resonance. Because the Tna.yTrn.riTn peak powers in
speech and music (see Section 12, articles 10 and 11) occur in the middle frequency range,
it is important that the speaker have high efficiency in this range, and the better speakers
have high force factors, which also reduce the transient distortion of the speaker.
MOVING-CONDUCTOR SPEAKERS
13-13
Direct radiator speakers normally reach their maximum efficiency in the low middle
frequency range, except when the effective baffle size is large so that the resonant fre-
quency is radiated effectively. In that case, if z& is small the maximum system efficiency
may occur at the frequency of mechanical resonance. The normal impedance is resistive,
or largely so, in either case. (See Fig. 4.)
+ 80
40 60 80 100 2OO 400 600 lOOO
Frequency Jn Cycles per Second
2000 4000
10,000
FIG. 4. Blocked and Normal (Primed) Resistance and Reactance of Moving-coil Direct^radiator
Speaker in Ohms
The system efficiencies hi the middle frequency range vary from roughly 1 to 20 per
cent in commercial direct radiator speakers. "The energy efficiency values are slightly
higher in the middle frequency range and exceed 90 per cent at the mechanical resonant
frequency in some designs.
ENCLOSURES. Direct radiator speakers are often placed in enclosures to contain
and control the radiation from the rear surface of the diaphragm. If the enclosure is
complete, that is, has no vents, it is sometimes called a "total enclosure" (see Enclosed
Back Piston, article 1). The rear radiation may be put to use by permitting it to escape
from the enclosure after first modifying it in phase and magnitude by a suitable acoustic
network. When the vents, or ports, which radiate the energy from the rear of the_ di-
aphragm are close to the front surface of the diaphragm, the mutual impedance isjhigh.
In this case the phase of the rear radiation is critical but gives rise to maximum radiation
when it is properly controlled (see article 2) .
When the length of the radiated wave is large compared with the enclosure dimensions
the acoustic parameters may be considered "lumped." A single cavity enclosure with a
port may then be considered to add a compliance corresponding to that seen by the
diaphragm with the port blocked or covered, which is in series with the speaker compliance.
The enclosure compliance is shunted by the effective mass and radiation resistance of the
port. The latter values are those referred to the speaker diaphragm. The frequency of
the two resulting low-frequency modes may be computed very approximately by neglect-
ing the mutual reactance term arising from the coupling of the external radiating surfaces
of the diaphragm and port through the mutual fluid impedance. The real part of this
mutual impedance must, however, be included in any accurate calculation of the total
radiated power. . . .^
The vented enclosure may be used to maintain uniform radiation down to lower fre-
quencies than those radiated effectively by a total enclosure of identical volume, or it
may be used to provide a rise in the radiation near the cutoff frequency of the mvented
enclosure. In practice it is common to provide a compromise between these two by so
choosing the speaker and enclosure parameters that the resulting two modes of the simple
structure described above occur approximately one-half octave below and above the mode
of the speaker and enclosure with blocked port. The augmented low-frequency radmtiom
is obtained with substantially reduced non-linear distortion since most of the radiation is
from the port, which need have no variable or non-linear parameters, and the diaphragm
displacement is appreciably reduced. » , , , , -,. * i
The rear of the diaphragm is sometimes coupled to a highly absorbent kne approximately
one-quarter wave long near the cutoff frequency of the acoustical system. The hne ab-
sorption should be low in the frequency interval in which the line is between three-quarters
and one wave long and increase rapidly above the upper frequency of this interval to
suppress radiation which would otherwise be out of phase with the front radiation. When
13-14
ELECTROMECHANICAL-ACOUSTIC DEVICES
the line is one-quarter and three-quarter wave long it serves as an impedance inverter,
thereby raising the impedance seen by the diaphragm and reducing its amplitude for a
given total radiation.
HORN-TYPE MOVING-COIL (OR CONDUCTOR) SPEAKERS. To increase the
fluid resistance, r/, a horn may be used to couple the diaphragm to the acoustic medium.
Because of their greater throat resistance at low frequencies for a given size, hyperbolic-
exponential horns with T < 1 (see article 3) are normally used.
In the case of horn units the normal (electrical) impedance can be made quite uniform
(see Fig. 5) so that the force on the diaphragm is approximately constant if the source
voltage and impedance are constant.
1000
800
600
400
200
100
80
40
W 20
10
8
6
\
\
r
&/
30 40 60 80100
~&y»
200 400 600 1000 2000
Frequency in Cycles per Second
40006000 10000
FIG. 5. Relative Scalar Normal Impedances of Typical Loud Speakers. (All arbitrarily adjusted to
have the same impedance at 400 cps. Reactance of an inductance and capacitance plotted for com-
parison.)
The diaphragm is made to resonate an octave or two above the horn cutoff frequency.
The stiffness reactance of the diaphragm assembly then reduces the effect of the mass
reactance of the horn near its cutoff frequency. At high frequencies, the stiffness of the
sound chamber may be made to reduce the effect of the mass reactance of the diaphragm.
The fluid resistance is adjusted to the desired value by proper choice of the ratio (£<;/£*).
These factors make possible the design of a horn having uniform response over an extended
frequency range.
At low frequencies, irregularities in response result from the variation in throat imped-
ance of a horn of finite length. The resonant frequencies of the horn near its cutoff fre-
quency also give rise to transient distortion. By using a horn unit having a large force
MAGNETIC-AEMATUEE SPEAKERS
13-15
factor and by proper choice of the other elements, the steady-state variation in response
and the transient distortion may be made negligible.
At high frequencies destructive interference occurs in the sound chamber since its dimen-
sions are of the order of magnitude of the length of the sound wave. The horn throat is
therefore sometimes so constructed that the difference in path length from different parts
of the diaphragm to the throat is a minimum. The use of a phase equalizing plug for this
purpose is shown in the horn unit of Fig. 2. At very high frequencies the diaphragm no
longer behaves as a rigid piston, and this alters the response of the unit.
The minimum compliance of the sound chamber is limited by its minimum volume, TV
This volume must be adequate to provide ample mechanical clearance at low frequencies,
where the diaphragm amplitude is a maximum, and to limit the distortion which results
from "finite" sound pressures.
Armature
Extension'
7. MAG1TOTIC-ARMATDEE SPEAKERS
"A magnetic-armature speaker is a magnetic speaker whose operation involves the
vibration of the ferromagnetic circuit. (This is sometimes called an electromagnetic
speaker.)" Numerous magnetic-armature designs
have been proposed. The principle of operation of
this type of speaker is analogous to that of moving-
conductor speakers, and equations for the latter
apply to this type if the appropriate value of zu is
used. They differ principally in the fact that the
conductor does not move, which permits the use of a
large conductor volume. In practice, high loudness
efficiencies can be obtained in a limited frequency
range with a magnet having moderate magnetomo-
tive force. The efficiency at very high frequencies
is normally poor because of losses in the armature.
The very low-frequency response is limited by the
stiffness required to give adequate armature sta-
bility. The current displacement curve is linear
over a very limited range and gives rise to appreci-
able amplitude distortion.
BALANCED-ARMATURE MAGNETIC
SPEAKER. A cross-sectional view of a unit of this
type is shown in Fig. 6. The speech current flows
through the stationary coil which surrounds the
armature. It increases the effective flux through two
(diagonally located) gaps and decreases it in the
other two gaps. The steady flux, <£>o, is increased
and decreased by an amount <£ = 4acNi/Gt gausses,
; Laminated
PoSe Piece
Fia. 6. Balanced Armature Speaker
where N is the number of turns on the coil, i is the current through the coil in abamperes,
and (Ft is the effective reluctance of the alternating flux path.
The total effective force on the armature, acting at the magnetic force center, is
4- <
87T.4
ffi
(8)
where F is the rms force in dynes and A is the effective area in square centimeters at each
gap and jSo is the steady or undisturbed flux density. For small amplitudes the reluctance
of the alternating flux path is approximately constant, since most of the reluctance is in
the gap, and the reluctance of the permanent magnet path is large.
The assumption is usually made that all the elements of the circuits and the force factor
are constant. This is approximated only when the amplitude is small. When the arma-
ture is in the undisturbed center position, it is in a state of unstable equilibrium. The
application of a force results in a force tending to increase the displacement. This property
is called negative stiffness or compliance. (See Section 5, article 30.) It here results from
the fact that the torque on the armature is proportional to the square of the flux density.
Therefore, it increases more rapidly at the tip that is approaching one magnet tip than
it decreases at the tip that is receding from the other magnet tip. Since the force varies
with the square of the flux density, and the density varies almost inversely with distance
between the armature and magnet tip, the stiffness can be considered a constant only for
small displacements. The positive value of Cm is, therefore, the difference between the
positive diaphragm (and fluid, if any) compliance and the negative compliance. Stability
13-16 ELECTBOMECHANICAL-ACOUSTIC DEVICES
of the system requires that the rate of change of force with displacement be less than the
coefficient of stiffness. The further assumption is made that the lever arm has infinite
stiffness. In practice, resonances of this arm play a large part in modifying the mechanical
impedance at high frequencies.
The steady-state solution for this speaker is the same as that of eqs. (5) and (b;. In
this case zn = 4faN/(R; for the more exact theory 012 is considered complex.
The principle of operation is analogous to that of the moving-conductor speaker. Equa-
tions for the latter apply if the above value of z\i is substituted. A large conductor volume
is normally used to increase the force factor. This makes the inductance of the electrical
circuit much higher than in moving-con speakers. For this reason, the normal impedance
varies over wide limits. The normal impedance is proportional to frequency over much
of the frequency range, as shown in Fig. 5. The rise in impedance above the value pre-
dicted on this basis at the high-frequency end, in this particular speaker, was due to
electrical resonance. The speaker was of the high-impedance type, and the inductance
and distributed capacitance resonated at the high-frequency end. This is normally the
case in high-impedance speakers of this type, and its effect must be included in any com-
plete performance analysis.
BIPOLAR MAGNETIC-ARMATURE SPEAKER. This type of speaker consists of
a steel diaphragm mounted near the two ends of a U magnet. The speech current flows
through the stationary coils which surround the two pole pieces. If the current through
the two coils, connected in series, is / sin cot, and the coils have N turns, the alternating
flux is <£ = 4 sm ^ , where I is the maximum value of the current in abamperes, and
(R
(R is the effective reluctance of the alternating flux path.
The total effective force F acting at the magnetic force center is
~
(HA
(R2A
(R2A
^ }
The first term on the right is a constant force; the second is the useful component which is
proportional to <fr> and to the signal current. The last two terms are distortion terms and
are minimized by making <£o » <£.
The force factor 212 = 2faN/(R. The more exact theory includes the case in which 212
is complex.
The principle of operation is analogous to that of the balanced-armature magnetic and
moving-conductor speakers. The equations for these speakers apply to the bipolar
magnetic armature if the value of 212 given above is used.
8. CONDENSER SPEAKERS
"A condenser speaker is a loud speaker in which the mechanical forces result from electro-
static reactions." Speakers of this type have a movable conducting electrode which serves
as the diaphragm and is mounted close to a perforated fixed electrode or between two
perforated fixed electrodes.
TWO-ELECTRODE CONDENSER LOUDSPEAKER WITH MECHANICAL CIR-
CUIT HAVING ONE DEGREE OF FREEDOM. One speaker of this type has a movable
and a fixed electrode separated by a thin dielectric as shown in Fig. 7. The force of attrac-
tion between the electrodes as the charge
varies provides the actuating force for the
movable electrode which is used as the
diaphragm.
The equations for a system of this type
are developed in Section 5, article 32. The
steady-state equations for a single sine-wave
" Metal Leaf Diaphragm
Rough Punched Holes
(Not Burred)
FIG. 7. Condenser Speaker
applied voltage are:
0 =
+
+
(100)
(10b)
where 212 = — ^rr = —7 • The force factor therefore varies directly with the polarizing
CtfCo»o fcjcfo
voltage, EQ, and inversely with the frequency and no-signal separation of the electrodes, do-
The minimum value of the separation is determined by the maximum low-frequency
TELEPHONE RECEIVERS (EARPHONES) 13-17
amplitude, and it must be large in comparison with the amplitude if non-linear distortion
is to be avoided.
The radiated acoustic power is &r/ X 10~7 watt, where * is given by eq. (116) and rf by
article 2. The diaphragm does not move as a piston. Therefore, a generalized velocity
based on the type of deformation here obtained must be used.
Because the blocked impedance of the speaker is that of a capacitance, G, the normal
impedance varies inversely with frequency over much of the frequency range. Therefore,
uniform response and high efficiency are difficult to obtain. The impedance of the elec-
trical circuit is sometimes altered to improve the response.
9. PNEUMATIC SPEAKERS
"A pneumatic speaker is a loudspeaker in which the acoustic output results from varia-
tions of an air stream." It is of the irreversible or relay type. The definition of efficiency
for reversible speakers is not used in this case, since the efficiency, as defined for them, can
exceed 100 per cent because no account is taken of the power used to compress the air.
Any type of loudspeaker motor may be used to drive a very light balanced valve which
modulates an air stream.
These units permit the generation of large acoustic powers. The valve and valve parts
give rise to spurious noises that are difficult to eliminate. When large acoustic outputs
are generated, there is appreciable "finite" amplitude distortion in the types that have
been made.
10. TELEPHONE RECEIVERS (EARPHONES)
Telephone receivers are so constructed that they operate directly into the ear cavity.
The fluid impedance of the ear cavity varies appreciably from ear to ear, particularly at
high frequencies. If there is no fluid leak between the ear "cap" of the receiver, which
held in contact with the ear, and the ear, the fluid impedance is approximately that of a
6-cms cavity at frequencies in the middle and lower frequency ranges. At high frequencies,
the ear cavity resonates and the fluid resistance of the cavity increases. If there is a fluid
leak between the ear cap and ear, the fluid resistance of this leak must be considered at
low frequencies where it tends to reduce the pressure in the cavity.
It has been found that a good compromise design for most ears is one in which the dia-
phragm displacement is independent of frequency. At low frequencies this gives constant
pressure in the ear cavity if -there is no fluid leak. Since the magnitude of the reactance
of the ear impedance substantially exceeds the resistance below 1000 cps, the power sup-
plied to the ear and the efficiency, as defined for other transducers, are not satisfactory
performance criteria. The pressure squared, produced at the end of a non-dissipative
cavity or "coupler/' per unit power available from an ideally terminated source, is a com-
mon performance criterion. A &-cc coupler is used for ear cap or external earphones and a
2-cc coupler for insert receivers which are placed in the outer ear canal and thereby reduce
the volume of the cavity between the receiver and the eardrum.
MOVING-CONDUCTOR TELEPHONE RECEIVERS. Both moving-coil and ribbon
telephone receivers are in use. The construction of one type of moving-coil receiver is
similar to that of the microphone shown in Fig. 3, p. 13-24. The values of the circuit
elements differ from those used in the microphone, in order to give as nearly as possible
constant diaphragm amplitude at all frequencies with a constant-voltage source.
t If the mechanical circuit consists only of the stiffness and resistance of the diaphragm,
and the combined mass of the diaphragm and moving coil, its "force" equations are given
by eqs. (6). The displacement s = *//«, where a is given by eqs. (6), Since z& is a con-
stant, if zn is made approximately constant, 2*2 must vary inversely with frequency for
the diaphragm displacement to be independent of frequency. This requires that the
diaphragm have stiffness reactance over the range of uniform response. This is obtained
by placing the resonant frequency of the diaphragm near the maximum frequency to be
transmitted. Under these conditions the normal impedance of the receiver is fairly uni-
form below the frequencies near the resonant frequency of the diaphragm. The force
is therefore nearly constant. The displacement of the diaphragm is small, and hence the
13-18 ELECTROMECHANICAL-ACOUSTIC DEVICES
efficiency of the receiver is poor when the resonant frequency and stiffness are high. It
is also difficult in practice to obtain very high resonant frequencies.
To improve the efficiency and yet maintain uniform response, additional mechanical
circuits are sometimes coupled to the diaphragm. The resonant frequency of the dia-
phragm itself is lowered, and the value of the mechanical elements is chosen to give uni-
form diaphragm displacement.
If the mechanical impedance is large in comparison with the ear cavity impedance, the
latter may be neglected. In general, it may be neglected only for approximate calcula-
tions. The impedance of the fluid between the diaphragm and the ear cap must also he
considered in any complete analysis.
MAGNETIC-ARMATURE TELEPHONE RECEIVER. The theory of operation
corresponds to that of magnetic-armature loudspeakers given above. The first center
moving mode of vibration of the magnetic diaphragm in the early type of telephone
receiver occurs near 1000 cps. Near this frequency, the amplitude is large and the pressure
in the ear cavity is large. Below this resonance region, the diaphragm has approximately
constant stiffness or compliance, and the amplitude is fairly uniform. At frequencies
above the resonant region, the displacement decreases and goes through a series of
decreasing maxima at higher modes of vibration. In more recent types there is a thin
film of air at the back of the diaphragm which is coupled to an auxiliary acoustical
network. The parameters are chosen to give uniform pressure at the bottom of the test
cavity or coupler up to 3000 cps in telephone hand sets and up to 4000 cps in some
military types.
PIEZOELECTRIC TELEPHONE RECEIVERS. The high frequency at which the
fundamental mechanical resonant frequency of a small Rochelle salt crystal occurs permits
its use as a motor or motor and diaphragm in a telephone receiver. The large variation
in normal impedance with frequency makes the response more dependent on the source
impedance than it is when the normal impedance is constant.
11. PERFORMANCE AND TESTS
One criterion of the excellence of a complete sound-transmission system is its ability
to produce the same space-pressure-time pattern at the ears of the listener that would be
experienced if he were immersed in the sound field in the region of the original sound.
This can be achieved with substantially complete realism in a binaural system in which
two transmission links couple two properly mounted pressure microphones to two broad-
band telephone receivers placed on the ears of the listener.
In practice there is a growing tendency to apply a second criterion, namely the ability
of a system to provide reproduction which is judged to be pleasant by a jury selected on
the basis of scientific sampling of the public or the ultimate listening group. This second
criterion has grown in importance for a number of reasons. One is that most listeners
prefer loudspeakers to headphones, thus introducing complex effects due to coupling the
loudspeaker to the ears of the listener via the listening room. Probably the most important
reason for choosing pleasantness as the criterion of excellence is that radio and phonograph
systems have in large measure attained the stature of an art medium in their own right.
This has led to extensive work on the design of new types of studios and the development
of new pickup techniques, all intended to please the listener in his home.
Though the complete test of a speaker is a complicated process, all the objective
measurements have as their goal a satisfactory correlation between their results and those
of properly conducted listening tests. Thus the ear becomes the final arbiter of the excel-
lence of a sound system.
For discussing the aural performance it is desirable to use terms descriptive of the
frequency ranges and of certain characteristics of the reproduced sound. As a group these
terms constitute the imagery by which sound systems are described. They relate princi-
pally to two important frequency regions: 400 to 800 cps, which contains most of the energy
of speech and music; and 2000 to 3000 cps, where the energy components contribute most
strongly to the loudness. The first region is located in what most listeners classify as the
low middles. A speaker with normal low middles is said to have "body," while an excess
is "muddy," and a deficiency sounds "thin." When the second range, in the lower highs,
is normal, reproduced sound is "crisp"; an excess introduces "bite" and is "brilliant"; a
deficiency reduces articulation and loudness and, if no extreme highs are present to provide
"spit," may yield a "mellow" speaker.
The whole range is conveniently divided into the very low frequencies, below 100 cps,
lows from 100 to 250 cps, lower middle from 250 to 800 cps, upper middles from 800 to
2000 cps, lower highs from 2000 to 4400 cps, middle highs from 4400 to 8000 cps, and
PERFORMANCE AND TESTS
13-19
extreme highs above 8000 cps. The boundaries are quite arbitrary and win depend on
the auditor, listening environment, and program material.
> OBJECTIVE PERFORMANCE CRITERIA. Loudspeaker performance is determined
to a large extent by the response, efficiency, directivity, distortion, power capacity, and
impedance. The relative importance of these and other less important performance
criteria depends on the application involved.
The response is that characteristic of the acoustic output, expressed as a function, of
frequency, to which a particular aural effect is closely proportional. The type of response
will depend on the use to which the speaker is put. For speakers used outdoors or for very
directional speakers the free space axial sound pressure level, as a function of frequency,
is used and is called the sound pressure response.
For use indoors the sound pressure level is determined by the total acoustic power
radiated and by the shape, size, and acoustical impedance of the room and its contents.
Thus the effect of the speaker alone is approximated by the total radiation, usually ascer-
tained by integration of the sound pressure measured in free space at fixed radius vector
and variable angle. The total radiation response is modified by the "room response" to
produce the desired effect on the ear, and it is often helpful to measure the rms average
sound pressure in a room which is representative for the intended applications of the
speaker. This mean pressure (corresponding to the mean energy density) response has
good correlation with the aural effect when the measuring room is also that used for
listening.
In Fig. 8 are shown the sound pressure, total radiation, and mean energy density re-
sponse curves for a direct radiator speaker in a finite baffle. The excess of high frequencies
+10
+
01
» —5
8
u
c
5-15
I
|-20
1
2~~
-30
-35
-40
Axial Sound Pressure, Free Space
_ Total Radiation, Dead Room
- — - — - Mean Energy Density, Average Room
40 60 80 100
200
40OO 60OO 10000 20000
400 600 10OO 2OOO
Frequency in Cycles per Second
FIG, 8. Three Types of Response-frequency Curves for a Direct Radiator Speaker in a Finite Baffle
in the pressure response is due to directionality, and the difference between the second
and third is due to the "response" of the room.
The system efficiency of speakers has been discussed in article 5. The loudness effi-
ciency of two speakers is compared using a generator of constant emf and impedance,
attenuation being inserted in the amplifier for the louder speaker. This judgment is
usually the first of any listening test. It is becoming standard practice to test speakers
with a source whose internal impedance is equal to its rated load impedance. The basis
of stating the input to the speaker is conveniently the maximum power that may be taken
from such a source, and it is called the power available to the speaker.
The series of sound pressure-frequency response curves run at various azimuths depict
the directional characteristics of the speaker. Another clue to the directivity is obtained
by comparing the sound pressure and total radiation response curves (see Fig. 8). When
the wavelength is long compared to the size of the radiator, the radiation is uniform, and
th§ curves should coincide. The differences at higher frequencies then indicate the magni-
tude of the directional effects.
If the listener's ear is relied on completely to select speakers having high loudness and
(apparent) bass and treble response, there usually result speakers having large amounts of
13-20 ELECTROMECHANICAL-ACOUSTIC DEVICES
800
600
400
300
non-linear, transient, and frequency response distortion. The need for quantitative tests
is indicated by Fig. 9, which shows
the non-linear distortion in the sound
pressure of a typical 12-in. speaker
mounted in an 8 by 8 ft baffle. The
speaker has an equivalent piston
diameter of 10 in., a high force factor,
and a voice coil 7/ie in. long moving
in a gap with a 3/s-in. top plate.
The curves are typical of commer-
cial direct radiator speakers. Ap-
proximately half the distortion at
low frequencies is due to the non-
linear force displacement curves of
the diaphragms. The remainder is
due to the non-linear average-fhix-
displacement curves of the driving
mechanism.
Since these curves are representa-
tive of commercial practice they are
of interest in indicating the amount
of distortion the untrained listener
will tolerate. Speakers designed to
give less distortion for a given cost
will have less loudness efficiency, and
less apparent bass response.
Distortion curves of horns show
distortion of the same order in the
middle frequency range. About a
third of an octave above the theoret-
ical cutoff frequency, the distortion
begins to rise, and below cutoff usu-
ally considerably exceeds the distor-
tion for direct radiator speakers.
This distortion largely accounts for
the horn's sounding as if it radiated
effectively below its cutoff frequency.
For a more complete discussion of
testing methods see the references in
the bibliography marked "tests."
Another measure of distortion is
the intermodulation of two signals
of non-harmonic frequencies produc-
ing inharmonic modulation products.
Because the annoyance of this type
of distortion is extremely high, much
smaller amounts may be tolerated
than with non-linear distortion.
Though the technique is not yet
standardized, a useful procedure is
to fix a low-frequency signal at a
large value while a variable high-
frequency scanning signal of much
smaller value is applied through a
linear combining circuit. A plot of
the sound pressure due to the scan-
ning signal and that due to the
modulation products affords a means
of assessing the audibility of the
modulation products. It is impor-
tant that this be done as a continu-
ous function of frequency in order
not to miss regions of large distor-
tion. This is shown in Fig. 10 for
an experimental direct radiator
40 50 60 80 100 ISO 200 300 400 500
Frequency fa Cycles per Second
Fio. 9. Steady-state Non-linear Distortion in Moving-
coil Direct Radiator Speaker
BIBLIOGRAPHY
13-21
with a 12-db difference between power available for low- and high-frequency
signals.
The power rating of a loudspeaker is intended to provide the user with a yardstick by
which he may set operating conditions to insure trouble-free life at any input up to the
maximum. While this rating may be limited by distortion, thermal overload, or mechan-
ical overload, the latter two are usually controlling. Thus the power rating usually sets a
limit above which mechanical failure may be expected to occur. In one method of specify-
ing this power, a saturating signal of a variety of program material is supplied to an am-
plifier of adjustable saturation power, used as the source. The rating power is that below
which failure will not occur within, say, 100 hours for at least 90 per cent of a group of
speakers. Thus the rating is essentially in terms of an amplifier whose output will be
safely handled. In another method of rating, the amplifier has a much greater rating power
than the speaker and is supplied a
synthetic signal, such as noise, warble
tone, or multitone. These have rea-
sonably constant spectral composition
and peak-to-rms ratio, and the power
is increased until the 100-hour failure
point is reached. Though neither
method is yet standardized, it is
nevertheless the intent of both to
provide a realistic and useful value.
A final important characteristic of
a speaker is its impedance. Both
modulus and angle usually exhibit
considerable variation with frequency,
and the problem is to connect this
load to a resistive source of essentially
constant impedance. When properly
connected, the source is able to deliver
to the load the maximum program
energy consistent with distortion re-
quirements. In practice this "con-
nection" impedance is selected by the
manufacturer on the basis of his listen-
ing tests and experience. It may be
called the rating impedance of the
speaker, and it indicates the tap on
the amplifier output to which the speaker should be connected. It is not necessarily the
value at 400 cps, or the minimum in direct radiator speakers. Besides its use in deter-
mining speaker connections, the rating impedance is often used as the generator resist-
ance in speaker tests.
1—20
400 700
2K 4K
Frequency . CPS
20K
FIG. 10. Modulation Products for Experimental 12-in.
Direct-radiator Speaker in Infinite Baffle. Available
power input, 100 cps fixed, 16 watts; scanning signal, 1
watt.
BIBLIOGRAPHY
American Standards ^Association, Standard C16.4-1942. (Tests.)
Ballantine, S., Proc. I.R.E., Vol. 23, 618 (1935). (Tests.)
Barnes, E. J., W.B., VoL 7, 248, 301 (1930). (Tests.)
Barrow, W. L., J.A.S.A., Vol. 3, 562 (1932).
Bostwick, L. GM J.A.S.A., VoL 2, 242 (1930). (High-frequency horn unit.) B.S.T.J., VoL 8, 135
(1929) (Speaker tests.)
Von BraunmuhL H. J.t and W. Weber, AJbw. Zeits., VoL 2, 135 (5/37). (Annoyance of distortion.)
Chinn, H. A., and P. Eisenberg, Proc. I.R.E., VoL 33, 571 (9/45). (Listener preferences.)
Cosers, C. R., W.E., VoL 6, 353 (1929). (Hornless speaker.)
Davis, A. H., Modern Acoustics. (General.) ,„«„,«
Edelman P E Condenser Loud Speakers with Flexible Electrodes, Proc, I.R.E., VoL 19, 256 (1931).
Fletcher, H., Proc. I.R*E., Vol. 30, 266 (6/40). (Role of hearing,)
Gerlach, E., Phynk. Zeit., VoL 25, 675 (1924). (Ribbon speaker.) J0_,_ - T w
Greaves, V. F., F. W. Kxanz, and W. D. Krozier, The Kyle Condenser Loud Speaker, Proc. I.R.E.,
Hannie W., Wi&senschafitickt VerSffenttickungen aus dem Siemens Konzem, VoL 10, 73 (1931), abo
VoL 11, 1 (1932). (Hornless and condenser speaker.) ,
Hanna, C. R., Proc. I.R.E.* Vol. 13, 437 (1925). (Balanced-armature magnetic speaker.) J AI.E.E
VoL 47, 607 (1928). (Horn unit.) Theory of the Electrostatic Loud Speaker, J.A.S.A., VoL 2, 143
Hartmann, C. A., and H. Jacoby, Elek. Nach. Tech., VoL 12, 163 (1935). (Tests.)
I.R.E. Standards on Electroacousiics (1938).
Kellogg, E. W., J.A.S.A., VoL 2, 157 (1930) (speaker tests); VoL 3, 94 (1931) Cow-frequency radia-
tion) ; VoL 4, 56 (1932).
Kennelly, A. E., Electrical Vibration Instruments. (Tests.)
Knowles, H. S.t Electronics, VoL 4, 154 (1932); VoL 6, 240 (1933). (Tests.)
13-22 ELECTROMECHANICAL-ACOUSTIC DEVICES
McLachlan, N. WM Speakers, J.A.S.A., VoL 5, 167 (1933) (tests, speakers, and bibliography); W. B.t
VoL 9, 329 (1932), Vol. 10, 204, 375 (1933) (distortion.)
Meyer, E., Electroacoustics. (Tests, general.)
N^poL 11, 548 (1929); WissenschaMicke VerQff^Uchungen aus dem
Siemens-Konzern, VoL 9, 226 (1930); and Siemens Zeitscknft, Vol. 10, 562 (1930). (Speakers and
Oliver! D. A., IF. B., Vol. 7, 653 (1930); Vol. 10, 420 (1933)
Olney, B.f Proc. J.fl.k, Vol. 19, 1113 (1931) (speaker tests); /.A.S.A., Vol. 8, 104 (10/36) (enclosures).
Olson, H. F., Acoustical Engineering. (Construction, tests, general.) MOOO /-* i u
Olson H. F., and F. Massa, Applied Acoustics (speakers-tests); J.A.S.A., Vol. 6, 250 (1935) (telephone
receivers) ; Proc. I.R.E., VoL 21, 673 (1933) (telephone receivers.)
Pedersen, P. 0., J.A.S.A., Vol. 6, 227 (1935); Vol. 7, 64 (1935). (Subharmomcs theory.;
Rice, C, W,, and E. W Kellogg, /. AJ.E.E., Vol. 44, 982, 1015 (1925). (Hornless m.c. speaker.)
Schafer, 0., Hochf. u. Elek., VoL 44, 101 (1934). (Speaker test.)
Sehaffstein, G., Hochf. u. EUk., VoL 45, 204 (1935). (Speaker and tests.)
Schottky, W., Physik Zeit., VoL 25, 672 (1924). (Ribbon speaker.)
Seabert, J. D., Proc. I.R.E., VoL 22, 738 (1924). (Speakers.) .
Stenzel, H., Handbuchder experimental Physik, VoL 17/2, 254 (1933) (loudspeaker, general) jSZecirtscAe
Nach. Tech., Vol. 4, 239 (1927); Vol. 6, 165 (1929); VoL 7t 90 (1930); also, Zwt. tech. Physik, VoL
10, 569 (1929), and Ann. der Physik, VoL 11, 947 (1930) (directivity of radiators).
Vogt, H., Elec. tech. Zeit., VoL 52, 1402 (1931). (Test condenser speaker.)
Von Sehmoller, F., Telefunken Zeit., VoL 15, 47 (1934). (Subharmonics.)
Wagner, K. W., Die wissenschaftlichen Grundlagen des Rundfunkempfangs. (General and speakers.)
Wegel, R. L., J. AJ.E.E,, Vol. 40, 791 (1921). (Moving-coil and magnetie-armature theory.)
Wente, E. C., and A. L. Thuras, B.S.T.J., Vol. 7, 140 (1928) (horn unit); Vol. 13, 259 (1934).
Wheeler, H. A., and V. E. Whitman, Proc. I.R.E., Vol. 23, 610 (1935). (Test.)
Williams, S. T., J. Franklin Inst., VoL 202, 413 (1926). (Horn speaker.)
Wolff, I., and L. Malter, J.A.S.A., VoL 2, 201 (1930). (Directivity of radiators.)
Wood, A. B., Sound. (GeneraL)
MICROPHONES
By Hugh S. Knowles
A microphone is an electroacoustic transducer actuated by energy from an acoustical
system, and delivering energy to an electrical system, the spectral composition of the energy
in the two systems being substantially equivalent. They may be classified as to reversi-
bility, type of generator, acoustical quantity to which the output is proportional, and type
of directional characteristic.
Reversible microphones are those that are also capable of converting electrical into
acoustical energy, and they include moving-conductor (ribbon and moving-ooil) , variable-
capacitance (condenser), variable-reluctance (moving-iron) and piezoelectric (crystal)
generator types. The most important irreversible microphone is the carbon (variable-
resistance) type,
Reversible microphones may be treated analytically by the same equations used for
the corresponding loudspeakers, provided that the emf in the electrical mesh is set equal
to zero and a force is introduced into the mechanical mesh (see Loudspeakers, p. 13-11).
12. FORCE ON THE MICROPROS
In practically all microphones the electrical output is proportional to the net force on
the generating element; less common types are those directly sensitive to the particle
velocity (hot-wire) and to the temperature (pyroelectric) of the sound wave.
PRESSURE MICROPHONES. In pressure-responsive microphones the active sur-
face is moved by a force which is the integral of the pressure over it. The pressure will
deviate from that in the free wave owing to the effects of diffraction, cavity resonance,
and mechanical impedance of the active surface. The last effect is usually small, and the
others may be minimized or in some instances utilized by careful attention to the size
and shape of the microphone. The microphone response may be stated in terms of the
undisturbed pressure in the wave, or in terms of tbe pressure at the active surface; these
are respectively the field and the pressure response.
Diffraction effects are important when the maximum dimension of the microphone
becomes much greater than a tenth wavelength. For frequencies well above this region
the pressure will be doubled (6 db) over the undisturbed value unless the diaphragm im-
pedance is very low. Since diffraction effects are also functions of angle, large pressure-
sensitive microphones may be expected to be directional at the higher frequencies. Screens
are sometimes used to modify the diffraction effects.
When the active surface is recessed, the shallow cavity will exhibit a broad resonance
which may be used to improve the high-frequency response. Though "gains" of the order
MOVING-CONDUCTOR MICROPHONES
13-23
Gridded Cap
Diaphragm
of 5 db may be attained, the sensitivity to angle again introduces directivity. If the force
resulting from a wave of normal incidence is to vary less than 2 db from that at grazing
incidence, then the active surface should be recessed no more than 0.1 its diameter. At
the highest frequency to be reproduced the
diameter should be less than a half wavelength.
In Fig. 1 is shown a miniature condenser micro-
phone which approximates these conditions up
to over 3 kc.
PRESSURE-DIFFERENCE MICRO-
PHONES. When two points in space are
separated by a small fraction of a wavelength
the difference in pressure at these points ap-
proximates the product of the distance they
are separated and the pressure gradient in the
sound field. For this reason pressure-difference
microphones are sometimes loosely called pres-
sure-gradient microphones. (See also Ribbon
Microphones, in article 13.)
When both sides of the active surface are
exposed to a sound wave, the net force on it
depends on the difference between the forces on
the two sides. Let the acoustic path length
from one side to the other be Ij,. Then when a
wave of undisturbed sound pressure amplitude,
p, is incident on the microphone at an angle 8 FIG. 1. Miniature CoadeEtser Microphone
to the axis of symmetry, the magnitude of the
net force, /, is, assuming no gradient along the active surface, and also assuming that the
pressure difference may be replaced by the gradient,
If wZ& is sufficiently small,
Ct^fr COS &
cos B
(1)
(2)
Thus, up to frequencies for which the path difference h is an appreciable fraction of a
wavelength, the net force is proportional to that path difference and to the frequency.
When the wave front is spherical, the pressure gradient exceeds its value for a plane wave
by the factor [1 -f (c/wr)2]^, which is small for <ar large. When the wave front is that
due to a piston, the axial gradient contains terms dependent on the ratio of piston diameter
to microphone distance. However, when this ratio is less than 0.5, the wave front is
sufficiently spherical to permit the spherical wave correction factor to be used.
FLUID IMPEDANCE. Studies of reciprocity laws indicate that the force of the
wave is applied through a "generator impedance" equal to that into which the active
surface works when radiating the same wave fronts as those applied. See article 2 for
results for some simple shapes. In general this added impedance is predominantly mass-
like up to the high-frequency region.
13. MOVING-CONDTICTOR MICROPHONES
In this class electrical energy is generated by the motion of single or multiple conductors
in a magnetic field, as exemplified by ribbon and moving-coil types.
RIBBON MICROPHONES. The more important constructional details of a ribbon
microphone are shown in Fig. 2. The moving ribbon element is both diaphragm and con-
ductor; it may be 0.312 in. by 2 in. by 0.0002 in. and is corrugated to minimize spurious
modes of vibration. As a low-frequency approximation, the effect of the fluid impedance
is to add a mass of the order of magnitude of that of the ribbon; this added mass decreases
at higher frequencies. The mechanical system is resonated at a frequency below the range
to be reproduced, resulting in a mass-controlled device.
In pressure-difference responsive ribbon microphones, both sides of the ribbon are ex-
posed to the wave. Thus the net force at low frequencies is roughly proportional to the
pressure gradient and hence to the velocity in a plane wave. For this reason the term
velocity is sometimes applied to microphones of this type. However, it appears desirable
to reserve the term velocity to describe devices such as the Rayleigh disk in which the
13-24 ELECTROMECHANICAL-ACOUSTIC DEVICES
actuating force arises more directly from the particle velocity. Up to fairly high fre-
quencies both the force and impedance (mass controlled) are proportional to frequency,
leading to a constant ribbon velocity and hence constant generated emf. Control of the
response beyond this point is achieved by adjusting the size and disposition of the pole
pieces and other elements separating the two faces of the ribbon.
If one side of a ribbon microphone is shielded from the wave by a damped enclosure,
the device becomes pressure-responsive. With a sound pressure independent of frequency
the output is independent of frequency if the enclosure adds sufficient resistance to make
the effective impedance of the diaphragm substantially
resistive. Such a pressure-responsive ribbon microphone
is used principally with a pressure-difference responsive
type in a directional combination.
FIG. 2. Pressure-difference Rib-
bon Microphone.
FIG. 3. Moving-coil Microphone
MOVIN"G-COIL MICROPHONE. When the moving conductor is a moving coil,
there results a form similar to that of a moving-coil loudspeaker, as in Fig. 3. With the
net force in the mid and high frequency ranges largely due to that on the outside of the
diaphragm, the device is pressure-responsive in these ranges. In order to obtain uniform
coil velocity and hence response the moving system is designed to have substantially
uniform impedance. The diaphragm and coil assembly is resonated in the low-middle
frequency range.
Coupled circuits are used to maintain uniform response at the extreme frequencies. In
Fig. 3 the circuit elements leading through the tube t to the rear of the diaphragm are so
chosen as to achieve an increasing force at low frequencies to offset the increasing stiffness
reactance of the diaphragm. At high frequencies the stiffness reactance of the air film
under the dome and the impedance of the tuned cavity in the pole tip modify the impedance
of the diaphragm and coil assembly so as to maintain approximately uniform velocity.
Thus it is possible to attain a fairly uniform response from 40 to 10,000 cps.
It is possible to combine the output of adjacent pressure and pressure-difference micro-
phones in such a manner that directional patterns are obtained which are members of the
limaQon family of which the cardioid is a special case. Common types use moving-coil
pressure and ribbon pressure-difference microphones connected through suitable phase
and amplitude controlling networks.
14. CONDENSER MICROPHONES
Most variable-capacitance microphones are made pressure-responsive, with a mechan-
ical system tuned above the desired range. A frequency-independent driving force acting
upon this stiffness-controlled system results in a displacement independent of frequency.
Since the output emf is closely proportional to the displacement, a flat pressure response
is approached.
To the mass of the diaphragm is added the radiation mass, and to its stiffness, that of
the air film between diaphragm and rear electrode. See Fig. 1. The diaphragm, is of a
high-tensile-strength aluminum or stainless-steel alloy of the order of 0.00075 in. thick,
and is tuned by stretching, the smaller diaphragms being tunable to higher frequencies.
The resistance of the thin interelectrode air film materially reduces the magnitude of the
high-frequency resonant peak.
The small cavity and the high mechanical impedance of the condenser microphone
make it particularly suitable for calibration by reciprocity methods. Two similar micro-
phones whose comparative response is known are placed in a closed cylindrical volume of
which each forms an end; the output of one is noted when the other is electrically driven.
CBYSTAL MICROPHONES
13-25
As with all reciprocity methods, its success depends on the presence of a definite and
calculable acoustic element, which here is the compliance of the common volume, corrected
for microphone mechanical impedance. With careful control of acoustic and electrical
parameters, excellent reproducibility of results is attained. The upper frequency limit
may be extended to 15,000 or more cps by the use of hydrogen hi which the wavelength is
increased by a factor of nearly 4.
As reciprocity methods yield a pressure calibration, a correction for cavity resonance
and diffraction is necessary. When the condenser microphone is used as a free field meas-
urement standard, it is common practice to utilise these factors to extend the frequency
range, with electrical equalizers added for smooth overall response.
15. MAGNETIC-ARMATURE MICROPHONES
A magnetic-armature microphone is a moving-iron (variable-reluctance) device which
finds greatest application where raggedness and high output are the main desiderata. An
important use is in sound-power telephones (using no auxiliary source of power, such as
batteries), which place a premium on maximum transmission of intelligence. This is
achieved by resonating the moving system at two or more frequencies in the 1-3 kc band
in which maximum articulation is obtained for a given amount of energy. (For force
factor and force equations see article 7, Magnetic-armature Speakers.)
16. CRYSTAL MICROPHONES
In this type use is made of the piezoelectric properties of Rochelle salt, ammonium
dihydrogen phosphate, or more rarely tourmaline and quartz. The sensitivity may be
expressed in terms of the charge released for a given displacement of the driving point;
this depends but slightly on temperature. However, the dielectric constant of Rochelle
salt and hence the capacitance and emf generated changes considerably with temperature.
The effect of this capacitance change is minimized by operating the crystal in a high-
impedance circuit, or less frequently by shunting it with a fixed capacitance. The max-
imum operating temperature range is 40 to +130 deg fahr, and maximum output occurs
at about 72 deg fahr.
The maximum operating temperature range of ammonium dihydrogen phosphate is
—40 to +185 deg fahr. While the emf generated is greater than for Rochelle salt, the
smaller dielectric constant results in such small capacitances that the full output is difficult
to realize. The high resistances necessitated by the small capacitances also give rise to
electrical noise problems.
Since the emf developed by crystals depends on the displacement, a stiffness-controlled
system in which the displacement is substantially independent of frequency is used. When
the microphone consists of a pah* of composite plates
arranged as in Fig. 4 to form a sound cell, the resonant
frequency may range from 8 to over 40 kc.
When a single composite plate is clamped at three
corners and the fourth is driven by a small diaphragm,
the output voltage increases some 15 db over the sound
cell construction, but the resonant frequency is then re-
duced to a few kilocycles. The main use of this type is
for speech, in which case the output is allowed to rise
Composite Plates
Sealing Membrane
Mounts, Separating
and Damping Slabs
FIG. 4. Crystal Microphone ("Sound Cell" Type)
Plate
FIG. 5. Unidirectional Diapbragm-
driven Crystal Microphone
substantially at the fundamental resonant frequency of 3 or 4 kc. Auxiliary acoustic
meshes are used to obtain smooth response with reduced sensitivity in broad-band types
used for music.
13-26 ELECTROMECHANICAL-ACOUSTIC DEVICES
A single transducer element crystal unidirectional microphone is shown in section in
Fig. 5. When the slot is closed the microphone operates as a pressure type. (See Direc-
tional Characteristics, below.)
17. CARBON MICROPHONES
The carbon microphone, the most important irreversible microphone, is a ^variable-
resistance type involving loose carbon contacts. The sound wave actuates a diaphragm
which exerts a varying pressure on a large number of fine carbon granules, thus modulating
a bias current obtained from a d-c source. Usually the resistance and output voltage are
approximately proportional to the displacement, and so a stiffness-controlled system is
employed. Because of the difficulty of obtaining uniform response, the present^ uses of
carbon microphones are restricted to applications in which high output and "crisp "speech
quality are paramount, as in military equipment. Another factor militating against its
use for high-fidelity applications is the low signal-to-noise ratio, due to the random varia-
tion in contact resistance always present.
The small allowable size of the carbon button has been used to advantage in a close
talking pressure-difference microphone with marked noise-reducing properties. Designed
to be worn directly in front of the mouth, the microphone is immersed in the large pressure
gradient field of the talker, while the ambient noise has a much smaller gradient. Thus
the signal-to-ambient-noise ratio is improved, permitting intelligible communications from
such noisy locations as planes, tanks, and engine rooms.
18. DIRECTIONAL CHARACTERISTICS
It is often important to collect sound arriving from a desired region to the exclusion
of randomly incident sound, as in sound-reinforcing systems. The ability of the micro-
phone to accomplish this is determined by the dependence on, angle and frequency of the
field response. There are many measures of directionality, such as the ratio of output for
sound from the desired direction to the output for sound of random incidence of the same
total power, the ratio of the output for sound of random incidence in the front hemisphere
to that of random incidence in the rear hemisphere, or the ratio of the outputs at the angles
of maximum and minimum response.
Most commonly used microphones may be classified as non-directional, bidirectional,
and unidirectional. Since pressure is a scalar quantity, an ideal pressure microphone is
non-directional. In practice complete freedom from directional effects is achieved only
when the maximum transverse dimension is of the order of an eighth wavelength or less.
Since most microphones are operated at frequencies up to 4000 or more cps, this require-
ment necessitates a microphone a centimeter or less in diameter. To provide adequate
sensitivity microphones are made larger than the non-directional requirements dictate
and commonly have a diameter of 2 to 5 cm. In pressure-actuated microphones this
results in a non-directional microphone at low frequencies and a unidirectional one at high
frequencies. Screens are sometimes mounted near the diaphragm to alter the sound field
and make the microphone less directional.
The most common bidirectional microphone is the cosine pressure-difference or "gra-
dient" type exemplified by the ribbon microphone discussed above.
Most unidirectional microphones have a directional characteristic, which, if taken in a
plane through the principal axis, is given by eu — &n + e& cos 0. If the microphone has
separate non-directional (pressure) and bidirectional transducer elements, en and ej, are
their respective voltages and BU is their combined voltage. One type of unidirectional
microphone is a pressure-difference type in which a single transducing element is used
with a network to shift the phase of one of the pressures to alter the directional charac-
teristic. In this type &n corresponds to the voltage with no force contribution from the
rear network and et, to the voltage when the rear and front impedances are equal and the
microphone is bidirectional. By adjusting the impedance of the rear network the relative
values of en and ei may be altered to give various directional characteristics. Single trans-
ducer microphones of this type are commonly made with crystal or moving-coil generators.
19. PERFORMANCE AND TESTS
The most important performance criteria are the field response (see Fig. 6), directivity,
impedance, and inherent noise. Less important for general applications are the "dynamic"
range (the range from minimum pressure, limited by electrical noise, to maximum pressure
BIBLIOGRAPHY
13-27
limited by non-linearity or by structural strength), the ratio of the responses for near and
distance sources, termed the proximity index, and non-linear distortion.
OBJECTIVE TESTS. The field response of a microphone is a measure of the elec-
trical output, for a specified frequency, when immersed in a plane progressive ware. When
the effect of the impedance is considered, an expression of the form 20 log E/p — 10 log R
results, in which E is the open-circuit emf, in volts, generated by the microphone; p is the
undisturbed sound pressure, in dynes/ cm2; and R is the stated impedance of the micro-
phone. This relation takes into account the effect of impedance in permitting the use of
step-up transformers. For crystal and condenser microphones, R is sometimes assigned a
value corresponding to the maximum stated value of transformer secondary impedance
used with low-impedance microphones, usually from 30,000 to 100,000 ohms. This value
permits a fairer compari-
son of all types in terms
of the amount of amplifi-
cation necessary, referred
to an input grid.
The directivity is usu-
ally determined from field-
response curves taken at
various angles of inci-
dence, or from the field
response as a function of
angle with the spectral
compositiQn of the test
signal held constant.
Single-frequency, narrow-
band warbled or fre-
quency-modulated and
noise test signals are used.
Unidirectional micro-
-F5
--5
40 60 UDO
10000 2OOOO
200 4Q060O 1000 2QOQ 40OO
Frequency In Cyctes per Second
PIG. 6. Axial Response-freqiaency Curves of Three Microphones
phones should show
greater than 10-db front-
to-rear discrimination (15 db is a common value), while in the bidirectional (pressure-
difference) type the front-to-side discrimination usually exceeds 20 db over a large fre-
quency range.
To minimize frequency discrimination and reduce electrostatic and electromagnetic
induction in long microphone lines, broadcast-type microphones have impedances ranging
from 35 to 250 ohms, with a trend toward 150 ohms. These microphones are usually
operated into impedances ten or more times that of the microphone's. This results in
about a 3-db improvement in the signal-to-inherent-electrical-noise ratio over that ob-
tained when the load resistance equals the modulus of the microphone impedance.
The present technique of primary calibration is by means of the reciprocity technique
mentioned under Condenser Microphones, article 14. This yields a pressure calibration,
from which the field response may be derived by calculation or measurement (with scaled
models) of diffraction and cavity resonance effects. A microphone thus calibrated may
be used as a standard from which the response of other microphones may be obtained by
comparison, in absolute terms. The source may be a sufficiently distant loudspeaker with
very smooth response; or for special purposes an artificial voice is used to obtain field shape
and diffraction effects approximating those of a person speaking. Although it is possible
to obtain free-field reciprocity calibrations, much work remains to be done before tbe
precision and stability of the pressure reciprocity method can be attained.
SUBJECTIVE (AURAL) TESTS. As with loudspeakers, the final acceptability of a
microphone depends on subjective tests. A live or artificial voice may be used as a source
for two microphones being compared, the outputs being alternately connected to an addi-
tion system. Such qualities as naturalness, smoothness, presence, articralaton, ®& objexv
tionability of intermodulation distortion, loudness efficiency, and transient distortion may
best be compared by aural tests with a trained jury.
BIBLIOGRAPHY
Am. Stds. Assoc. Standard Z24.4-1938. (Calibration.)
Am Stds Assoc. Standard Z24.1-1942. (Terminology.)
Baerwald, H., J.A.S.A., Vol. 12, 131 (1940). (N°*e.)
Ballantine, S., J.A.S.A., Vol. 3, 319 (1932). (Calibration.) .
Bauer B. B., J.A.S.A., VoL 13, 41 (1941). (Unidirectional microphone.)
13-28 ELECTROMECHANICAL-ACOUSTIC DEVICES
Braunmuhl, H. J. von, and W. Weber, Hochfrequenztechnik u. Elektroakustik, Vol. 46, 187 (1935).
(Directional pressure-difference condenser microphone.) .
Cook, R. K., J. Research, National Bur. Stds., Vol. 25, 489 (1940), (Reciprocity.)
Crandall, I. B., Phys. Rev., Vol. 11, 449 (1918). (Condenser microphone.) .
Efflthora, H, E., and A. M. Wiggins, PTOC. I.R.E., Vol. 34, 84 (1946). (Gradient microphones.)
Foldy, L. L., and H. Primakoff, J.A.S.A., Vol. 17, 109 (1945). (Reciprocity.)
Gerlach, E,, and W. Schottky, Physik Zeits., Vol. 25, 276 (1923). (Ribbon microphone.)
Glover, R. P., J.A.S.A., Vol. 11, 296 (1940). (Cardioid unidirectional microphones.)
Harrison H fc , and P B. Flanders, B.S.T./., Vol. 11, 451 (1932). (Miniature condenser microphone.)
Marshall, R. N., and W. R. Harry, J. S.M.P.E., 33, 54 (1939). (Cardioid microphone.)
Massa, P., J.A.S.A., Vol. 17, 29 (1945). (ADP microphone.)
Olson, H. F., Elements of Acoustical Engineering. (General.)
Olson, H. F., R.C.A. Rev., Vol. 6, 36 (1941). (Reciprocity.)
Sawyer, C. B., Proc. I.R.E., VoL 19, 2020 (1931). (Crystal microphones.)
Schottky, W., Zeits. f. Physik, Vol. 36, 689 (1926). (Reciprocity.) _ .
Wente, E. C., and A. L. Thuras, J.A.S.A., Vol. 3, 44 (1931). (Moving-coil microphones.)
MAGNETIC RECORDING AND REPRODUCING
OF SOUND
By L. Vieth and H. A. Henning
The earliest record of magnetic recording is credited to Poulsen, who in 1900 described
his "Telegraphone." Since that time, though much has been learned and vastly improved
results have been obtained, extensive use of the method as a recording process of great
potentialities was not achieved until the war years of 1941-1945.
The magnetic recording method possesses certain unique advantages. The mechanism
may be simple to operate and rugged. The record can be played immediately after record-
lag and can be replayed practically any number of times. The recording may be erased
and the medium reused as often as desired.
Magnetic recording involves three fundamental operations or processes: (1) erasing;
(2) recording; (3) reproduction or playback. Erasing is the process by which the magnetic
recording medium is either neutralized or saturated to obliterate any signal previously
recorded. In the early phases of development saturation by a strong d-c field was used.
More recently neutralization of the medium by a high-frequency a-c field has been required
in conjunction with modern methods of recording with an a-c bias. Recording is accom-
plished by applying, through the recording head, the signal to be recorded superimposed
on a biasing current. The bias current may be either direct or high-frequency alternating
current. Considerations governing the choice of biasing and erasing methods are discussed
in article 21. The bias current is necessary to obtain a faithful recording of the impressed
signals. The medium, as it passes under the influence of the recording head, is magnetized
in proportion to the variations of the signal current, and this magnetization remains until
erased. Reproduction or playback is accomplished by passing the recorded medium over
a magnetically sensitive head, usually at the same velocity as in recording. The voltages
induced in the head are then amplified and equalized to obtain the desired frequency char-
acteristic. All these processes may be accomplished with the same head at some sacrifice
in performance.
20. ERASING, RECORDING, AND REPRODUCING ARRANGEMENTS
Physical arrangements by which the magnetic forces are applied to a magnetic medium
(usually in the form of a tape or wire) have taken several forms. They may be divided
into three broad classifications: (1) perpendicular magnetization, in which the direction
of magnetization is normal to the surface of the medium; (2) modifications of (1), which
alter perpendicularity somewhat; and (3) longitudinal magnetization in which the direction
of magnetization is parallel with the direction of motion of the medium. Transverse mag-
netization in which the direction of magnetization is parallel to the surface of the medium
and normal to the direction of motion is a fourth possible classification which will not
be considered here. Figure 1 illustrates schematically the three arrangements. Each
consists essentially of cores of high-permeability material surrounded by one or more
coils. Figure l(a) shows the perpendicular application of magnetic force to a medium in
the form of tape, moving between the poles, each consisting of one lamination in exact
alignment. Each pole is surrounded by a coil. A concentration of recording flux is obtained
by the small thickness of lamination in the direction of tape travel.
Figure 1 (&) illustrates a more efficient and practical modification of (a] . Much thicker
cores are used, which are in contact with opposite surfaces of the tape. Flux concentration
is accomplished by offsetting the poles in the direction of travel by an amount almost
ERASING, RECORDING, REPRODUCING PROCESSES 13-29
equal to their thickness. A coil surrounds the advance pole. The tape is therefore mag-
netized in a preponderantly perpendicular manner with a longitudinal component. Induc-
tion at short wavelengths is most pronounced on the side of the tape in contact with the
coil-bearing pole. Omission of the coil on the receding or following pole avoids a secondary
concentration of recording flu* as the tape leaves the influence of the recording head, thus
avoiding modulation of the already recorded signal. The schemes illustrated in l<a) and
1W require that intimate contact must be maintained by pressure against both surfaces
of the tape. Joints must therefore be carefully made, and the two surfaces must be uni-
formly parallel to insure good contact at all times. Furthermore, these two schemes are
of limited use on wire and are even less useful on non-magnetic tapes coated on one side
with magnetic materials. Figure l(c) shows an arrangement which applies magnetising
force longitudinally. Contact is made on only one side, and the principle is therefore
conveniently applicable to all forms of recording media A ring of permeable material
FIG. 1. Typical Magnetic Recording and Reproducing Arrangements
wound with a coil is provided with a small air gap at the point where it touches the record-
ing medium. A portion of the flux in the air gap passes through the medium. The result-
ing magnetization is substantially longitudinal. The concentration of flux is accomplished
by the use of very small gaps ranging from 0.003 in. to less than 0.0003 in., depending on
the medium.
Although all the above arrangements may be used for erasing, recording, and reproduc-
ing, it is expedient to alter their characteristics in the interests of one process or another.
Separate heads are frequently provided for each process. In each case it is important
that the magnetic action of the head in recording and reproducing be concentrated along a
line perpendicular to the direction of motion. The greatest concentration of active flux
lines is obtained for a given pole-piece arrangement when the tip reluctance of the record-
ing or reproducing pole piece is low. Poles or cores are usually laminated to reduce the
frequency discrirninating effects of eddy currents.
21. ERASING, RECORDING, AND REPRODUCING PROCESSES
RECORDING SPEED. The various systems used for driving the magnetic media
will not be discussed here. There are, at present, no standardized recording speeds, aad
in most applications the medium is moved past the recording and reproducing heads at
the slowest speed that will insure the desired high-frequency response. In practice these
speeds range from a few inches to several feet per second. In order to obtain a freqtkeacy
range of 10,000 cycles it is modern practice to employ recording speeds between 1 lfe and
5 ft per sec, depending on the properties of the recording medium and the methods of
recording.
ERASING. The process used to obliterate a previously recorded signal on a magnetic
medium is called erasing. In most applications the erasing operation is performed during
the recording process by a head located somewhat in advance of the recording head. There
are, however, instances in which it is more convenient to perform the erasure as an inde-
pendent operation.
A previous recording may be removed either by saturating the medium with a strong
d-c field or by neutralizing the medium with an a-c field of diminishing intensity. In the
13-30 ELECTROMECHANICAL-ACOUSTIC DEVICES
first process every portion of the medium entering the erasing head is carried to saturation
or a degree of magnetization exceeding the strongest recorded signal. The erasing head
may consist of a permanent magnet or an electromagnet supplied by direct current. In
certain designs the configuration of leakage flux lines around the head can cause a second
and reversed field to act on the medium as it leaves the head. Under such conditions the
initial saturation is followed by a partial demagnetizing operation, and the ultimate state
of the medium may be considerably less than fully saturated. As the optimum d-c record-
ing bias is determined by the magnetic state of the erased medium it is apparent that the
design of the erasing head influences the constants of the recording process.
It is now common practice in high-quality magnetic recording to erase by a neutralizing
or demagnetizing action. This is accomplished by subjecting each element of the medium
to a cyclicly varying magnetic field whose maximum intensity between the poles of the
head produces saturation. As the element moves away from the head it is subjected to a
continuously diminishing cyclic magnetization which leaves the medium in a neutral state.
A magnetizing force approximately three times the coercive force of the medium has been
found to be satisfactory. A field intensity of 1500 oersteds may be required to demagnetize
some of the modern high coercive force materials.
Some use has been made of an air-core coil for erasure of the lower-coercive-force
materials. The medium is drawn through the center of the coil, and a comparatively
low-frequency erasing current is required. If erasing is accomplished with the recording
head a higher-frequency
RECORDfMG FIELD, H
PIG. 2. Magnetic History of an Element of Recording Medium. Sat-
uration erase, d-c Bias.
current is used to provide
the necessary number of
reversals in the short
time the medium is within
the influence of the head.
In certain instances a
combination of d-c satu-
ration followed by partial
neutralization has been
employed. In such cir-
cumstances the recorded
signal is successfully
erased but there remains
a residual d-c component
on the medium which is
responsible for somewhat
increased distortion.
RECORDING. The
process of recording con-
sists of impressing on the
moving magnetic me-
dium a varying induction
which is directly propor-
^on-al to the instantane-
ous value of the recording
head current. The
.
cording head is usually associated with an amplifier so designed that the recording cur-
rents are independent of the impedance characteristic of the head. In most applications
recording currents are small and very little power is required. In certain applications
electronic amplification is not used and the recording current is obtained directly from a
carbon microphone.
The linear relationship between recording current and the resulting magnetization on the
medium is obtained by the use of a superimposed biasing field, usually by superposing a
biasing current on the recording current fed to the head. Without the bias the reproduced
signals are weak and very distorted. The biasing field is adjusted to a magnitude that
minimizes the distortion without introducing unnecessary background noise. The proper
value is usually slightly less than that which will yield the strongest reproduced signal.
Two biasing methods are available. It is now customary to use a high-frequency (super-
sonic) biasing current, and the greatest dynamic recording range may be obtained by this
method. In earlier applications a d-c biasing current was used; it is advantageous where
extreme compactness and simplicity of equipment are essential.
The magnetic processes involved during recording may be illustrated by hysteresis loops
such as those of Figs. 2, 3, and 4. These curves represent Bi (or B-H} vs. H, or intrinsic
induction vs, magnetizing force. They thus represent the fundamental characteristic of
ERASING, RECORDING, REPRODUCING PROCESSES 13-31
the recording medium. Each element of the medium, as it passes the recording point, is
subjected to a magnetizing field which is proportional to the algebraic sum of the instan-
taneous recording current and the biasing current. The element is then withdrawn from
the field. For long uni-
formly magnetized sec-
tions the resultant state
of each element of the
section would be repre-
sented by a point on the
Bi axis. The magnetic
state of an element of a
short magnet (because of
self-demagnetization) is
represented by a point on
an appropriate demag-
netization coefficient line.
The demagnetization co-
efficient line OA of Figs.
2, 3, and 4 may be called
the open circuit line, and
it defines the state of the
element when removed
from the head. When-
ever the element under
consideration is within
the playback head, the
self-demagnetizing field
is partially removed and
the magnetic state of an
element moves along a
FIG. 3. Magnetic History of aa Element of Recording Medium. Neu-
tralization erase, d-c bias.
reversible minor hysteresis curve which may be represented by a straight line such as Dd
in Fig. 2 to a steeper demagnetization coefficient line OB, The slope of line OB, which
may be called the closed circuit line, is determined primarily by the reluctance present at
the contact point of medium and head and thus is substantially independent of the recorded
wavelength. In longitudinal
recording the slope of the
open-circuit line OA is to
some extent a function of the
recorded wavelength, and
thus the self-demagnetization
is a function of frequency.
The effect on the frequency
response of this action may
be at least partially offset* by
the use of high-coercive-force
materials.
Figure 2 illustrates the
magnetic process of recording
with a d-c bias on a medium
that has previously been sat-
uration erased. During the
erasing process the saturating
field brings the magnetic state
of each element of tfee medium
\ to a point C on the hysteresis
\ curve. Assuming that the
element leaves the erasing
field without being subjected
to a reverse magnetization,
the magnetic state of the ele-
ment moves along the hys-
teresis curve CC'D to point
PIG. 4. Magnetic History of an Element of Recording Medium*
Neutralization erase, a-c bias.
D on the open-circuit line OA. Subsequently, when in the recording head, the state of
the element is represented by point d on closed-circuit line OB, and as the minor
hysteresis curve Dd traversed during this process is substantially reversible any applied
13-32 ELECTROMECHANICAL-ACOUSTIC DEVICES
recording field operating within this region leaves no change in impression on the
medium. If after saturation a d-c bias is applied, the state of the element is brought to
point E along the major loop, and this point is chosen to represent the midpoint of the
available operating range. Variations in the recording field will then produce correspond-
ing changes in magnetization. The combined action of the biasing field and the signal
field then operates over a substantially straight section DEF of the hysteresis curve. When
the element emerges from the recording head, its magnetic state returns along the minor
loop to the open-circuit line OA and subsequently, when in the reproducing head, to the
closed-circuit Hue OB along the same minor loop. Depending on the signal strength, the
path of this action is along nearly straight, parallel, and reversible minor hysteresis curves
Ijing between Dd and FO. Thus the flux induced during reproduction, for the state of
magnetization corresponding to a point on the closed-circuit line OB lying between 0 and d,
is practically linearly related to the applied recording field.
In Fig. 2, the point F represents one of the limits of the recording field which may be
applied to the medium without serious distortion. This is because minor hysteresis curves
have greater curvature after crossing the Bi axis and a minor hysteresis curve such as Gh
leaves the magnetic state of the element at gf instead of the required point g.
The operating range during recording at short wavelengths is also restricted wherever
the slope of the open-circuit line OA is a function of the wavelength. This is illustrated
in Fig. 2 by line OA', which might be the slope of the open-circuit line in a medium longi-
tudinally recorded at a short wavelength. The magnetic state of a saturated element is
then represented by the point Df. The recording field is thus restricted to operation over
the region between D' and F.
Figure 3 illustrates the magnetic process involved when a d-c bias is used with a com-
pletely demagnetized medium. The recording bias alone serves to carry the magnetic
state of the element along the normal magnetization curve ODEF to point E. The record-
ing signal operates about Et which is chosen as the midpoint of the linear part of the mag-
netization curve. Upon leaving the recording head the magnetization of the element
drops to line OA along one of substantially parallel hysteresis curves similar to and lying
between Dd' and F/'. The process is thereafter similar to that described for saturation
erase. If, at shorter wavelengths, the slope of the open-circuit demagnetization coefficient
line OA is reduced to OA', points d and / on the closed-circuit demagnetization coefficient
line OB are proportionately reduced. This results in an attenuation of the recorded signal.
It may be observed in Figs. 2 and 3 that the degree of magnetization of an element which
has been biased but is otherwise unrecorded is substantially the same in either process, and
also that the undistorted operating range is nearly identical. Because of these conditions
the background noise and dynamic range in either process are substantially the same, and
thus when operating with a d-c bias there is little advantage in providing extra equipment
to demagnetize the medium.
It is now customary to erase by demagnetization and employ a high-frequency (super-
sonic) biasing current during recording. The action of the high-frequency bias has been
variously explained. It is sufficient to say here that it serves the purpose of straightening
out the bend in the normal magnetization curve around the origin. The resulting action
is as shown in Fig. 4. The recording signal may then operate about the origin 0 and along
the entire straight portion of the curve between D and F. The remainder of the process
may be considered to be similar to that described for recording with a d-c bias on a demag-
netized medium except that the recording range is doubled. This represents a doubling of
the reproduced signal without an equivalent increase in background noise.
There is an even greater increase in signal-to-noise ratio inasmuch as the elimination of
the d-c biasing component of magnetization serves to reduce the observable background
noise. The biasing frequency employed in this method of recording is customarily quite
high and usually leaves no permanent impression on the magnetic medium. Wherever a
biasing frequency is recorded, it is beyond the range of the playback equipment and is not
reproduced.
In common with all methods of sound recording, magnetic recording introduces a certain
amount of distortion although modern magnetic recording systems are considerably im-
proved in this respect. Distortion is introduced during the recording process from several
sources. The most common source of distortion arises from the non-linear properties of
the recording medium. It is apparent from Figs. 2 and 3 that there is an optimum value
of d-c bias which will minimize curvature distortion. When using an a-c recording bias
there is a minimum value which is sufficient to eliminate the curvature of the normal
magnetization curve around the origin. Higher values than the necessary minimum may
be used, but there is no advantage to be obtained. Distortion resulting from intermodula-
tion between the bias frequency and the signal frequencies and their harmonics may be
ERASING, RECORDING^ REPRODUCING PROCESSES 13-33
kept outside the operating range by using a sufficiently high biasing frequency. When
recording with an a-c bias, distortion is increased by the presence of a residual d-c magnet-
ization which may be present either in the recording and reproducing heads or in the
erased medium.
A distortion may also be introduced by the recording head if the magnetizing field at
the head is not sufficiently concentrated. At higher frequencies it is then possible for
the recording signal to change while an element is within the influence of the head, and
the Clement will retain an impression of the strongest magnetizing force to which it is
subjected. The use of narrow recording gaps and modern high-permeability pole pieces
has greatly reduced this type of distortion.
REPRODUCTION. In the reproducing process the varying magnetization impressed
on the medium during recording produces a corresponding flux in the reproducing head. A
portion of this flux threads the coil, and its variation due to the motion of the medium
induces the signal voltage. Signal voltages are normally quite low, and considerable
amplification is required.
The process by which the reproducing head picks up the signal flux is essentially similar
for any of the heads of Fig. 1. The return path for all the signal flux in a magnetized
element approaching the reproducing head is through the air. The magnetic state of such
an element is described in Figs. 2, 3, and 4 by a point on an open-circuit demagnetization
coefficient line such as OA. As the element approaches the head some of the flux which
leaves the medium passes to the head. In the case of the head of Fig. l(a) a portion of
this flux threads the coil. The percentage of flux which threads the coil increases very
rapidly as the element comes directly under the thin lamination and decreases as rapidly
thereafter. Thus the total flux threading the coil is contributed by the magnetized ele-
ments under the thin lamination and those immediately adjacent. In the case of the
offset pole pieces of Fig. 1(6) the major contribution to the flux threading the coil is made
by the elements in the immediate region of the overlap point. Elements in contact with
one pole tip and remote from the overlap point are either insufficiently coupled or, at short
recorded wavelengths, are short-circuited by the pole tip and therefore do not contribute
to the flux threading the coil. The ring-shape head of Fig. l(c) operates in a somewhat
similar manner. The head serves as a return path for flux leaving the surface of the
longitudinally recorded medium. With the exception of flux from elements of the medium
in the immediate vicinity of the air gap, the return path does not include the reproducing
coil. Thus the flux which does thread the coil may be considered as being contributed by
the elements in the immediate region of the air gap.
When the recorded element is in position at the reproducing point its magnetic state is
described in Figs. 2, 3, and 4 by a point on the closed-circuit demagnetization coefficient
line OB. The slope of this line is determined by the total reluctance of the return path
for the element in question, and this reluctance is affected by the amount of contact
between the medium and pole pieces. The flux threading the coil is then equal to the prod-
uct of the Bi intercept of the point on OB, the normal cross-sectional area of the contributr-
ing elements, and an appropriate leakage factor. The contact reluctance of the narrow
pole-tip structure of Fig. l(a) is higher than that of the broad pole-tip structures of Figs.
1(6) and l(c). Therefore the slope of the closed-circuit demagnetization line OB will be
less in the former case and the flux threading the coil for a given magnetization of the
medium will also be less.
The open-circuit signal voltage at the reproducing head is proportional to the rate of
change of flux threading the coil. This factor in itself is responsible for a 6 db per octave
rise in the signal characteristic. There are, however, several other factors that enter
into the overall frequency response. (1) In both recording and reproduction the eddy-
current characteristics of the head may introduce some attenuation at higher frequencies.
(2) Following recording, the medium demagnetizes to a degree which is a function of the
length of the recorded magnets. In longitudinal recording the resultant attenuation is an
inverse function of the recorded wavelength. (3) In reproduction the response falls off
when the dimension of the recorded wavelength becomes comparable to the active region,
of the reproducing head. Although the region in which a magnetized element of the
medium may cause flux to thread the coil is not sharply defined, an effective dimension
may usually be assigned, and this dimension has been called the "slit width" because of
its similarity to the optical effect. In the ring-shape recording head experience has shown
that the slit width is from 10 to 40 per cent greater than the air-gap length. (4) In certain
reproducing heads, such as that of Fig. 1(6), the construction is such that the pole pieces
are somewhat active over their entire dimension. Thus there is in effect a secondary slit
width equivalent to the overall dimension of the poles which is responsible for irregularities
in the response at longer wavelengths.
13-34 ELECTROMECHANICAL-ACOUSTIC DEVICES
Lubeck has given, for ring-shape heads, a general expression for the open-circuit output
voltage
CD
—
X
where E and I are, respectively, the open-circuit output voltage and input current,
C = a constant for the particular system, N - number of turns in reproducing coil,
T> - linear speed of medium, s = effective "slit width" of reproducing header = a demag-
netization constant for the medium, X = v/f — wavelength of recorded signal, / « fre-
quency, and w = 27r/. The (electric to magnetic) frequency characteristics of the record-
ing and reproducing head have been neglected in this expression.
Figure 5, curve (1), shows an illustrative frequency response characteristic. The factors
determining the characteristic are independently plotted. It is seen that the function
sin TS/X which is the "slit width" characteristic plotted in curve (3) rises to a maximum
I
(3) THE CHARACTERISTIC 6-DB PER
- OCTAVE RISE AND EFFECT OF
"SLIT WtDTH*OF PLAYBACK HEAD-
><T^
\
I
i
\
^^
\
\\
\
^
^
^
(2) EFFE
DEMA6NE
OF M
S
:TOF
mZATl
EDIUM
V
^
,1
\
sf?
X
ON^
\
i
.x^
(0 RESPONSE AT
PLAYBACK HEAD"
\
i\
/S
VELOCITY
PER
= 24 INCHES
SECOND
i II \
S =O.OO2 INCH
T=O.O04- INCH
\
t
r
lA
0,4 Q.6 0.8 J
FREQUENCY
2 46
IN KILOCYCLES PER SECOND
8 10
20 30
FIG. 5. Frequency Response of a Longitudinal Recording. Open-circuit playback voltage for constant
recording current.
when the recorded wavelength is twice the effective slit width. Thereafter it goes through
a series of dips and peaks. In a practical head design where the working gap is very small,
the second and succeeding peaks are not reproduced because they lie in the region where
the demagnetization, curve (2), of the medium causes a high loss and they usually fall
outside the frequency range of associated electrical circuits.
At recording speeds in current use the slit width may be made sufficiently gtyia-U so that
sin 3rs/X can be replaced by the angle itself within the working frequency range. Under
these conditions
E
(2)
and it is seen that, except for demagnetization, the output voltage rises 6 db per octave
and is not influenced by the recording or reproducing speed or the width of the effective
slit.
It is usually necessary to introduce an electrical equalization in the associated recording-
reproducing circuits in order to obtain the desired overall frequency response. A major
portion of the equalization is assigned to the reproducing circuits where it is limited only
by the frequency spectrum of background noise.
When due consideration is given to the overload characteristic of the recording medium
and the energy distribution of the recording signal, some of the equalization, may be
introduced in the recording circuits.
SOURCES OF ICOISE. Background noise arises from a number of sources, many of
wfaich may be minimized in careful design. Among such sources may be listed amplifier
inim* thermal noise, external noise pickup in the reproducing head, crosstalk transferred
from & strong signal on adjacent turns of the medium when wound on the storage spool,
BQfteohanieal irregularities on the surface of the recording medium which affect the degree
RECORDING MEDIA 13-35
of contact with the reproducing head, variations in the magnetic properties of the medium,
and variations in the cross-sectional area of the medium. The remaining, and basic, noise
source appears to be caused by a random distribution of small magnetic inhomogeneities.
Some measurements at the reproducing head of noise from this source have indicated a
fairly uniform frequency distribution of noise voltage per cycle. In most cases, after
equalization, this background noise has a smooth character and so is not particularly
disturbing. Basic noise is a function of the degree of magnetisation of the medium. It
is very low for a medium which has been thoroughly erased by a-c demagnetization, but
it may be increased to a considerable extent by the presence of the a-c biasing flux. The
noise level may be considerably increased by the use of a reproducing head in which there
is some remanent magnetization, and the use of a d-c bias increases the noise markedly.
Wherever the noise is decidedly affected by the presence of recording bias, there is detect-
able, back of the signal, a noise which rises and falls with the magnitude of the signal. A
certain amount of such noise is not objectionable as it is partially masked by the signal.
22. RECORDING MEDIA
PHYSICAL FORMS. Most of the early magnetic recording equipment employed a
solid homogeneous steel wire or tape as the recording medium. Recent refinements in the
art of electroplating magnetic alloys and developments in the use of magnetic-powder-
coated paper and plastic materials have removed many of the restrictions on the form of
the recording medium. Although there are some technical differences between the media,
the choice of physical form in general is determined by the desired application.
Magnetic wire is generally used wherever a very long playing time is required or a com-
pact equipment is necessary. The wire diameter is limited only by the required breaking
strength, and diameters between 0.004 in. and 0.006 in. are most common. Splicing is
accomplished by tying a square knot which passes over a properly designed head without
difficulty. A longitudinal recording head is usually employed, and the wire rides in a
groove which is worn in the head. This method of recording is designed to distribute the
recording signal about the circumference of the wire and serve as a protection against
variation of the reproduced signal as the wire twists. There is, however, a considerable
variation in the strength of the recorded signal around the circumference of the wire,
particularly at short wavelengths, and it is fortunate that smooth, round wire does not
evidence a random twisting when properly used. The chief disadvantage of the use of
wire is the tendency to uncoil, snarl, and kink whenever a free end becomes loose. For
this reason it is advisable to mount the wire in a magazine containing the supply and take
up reels and remove the magazine as a unit wherever record storage is required.
Magnetic tape, either solid or plated, is most useful for applications requiring a con-
tinuous record-reproduce-erase cycle. In such applications the tape is prepared in the
form of an endless belt which is spliced, at the junction point, with a butt weld. When-
ever a more extended playing time is required the tape is reeled like motion-picture film.
Recording equipment has been commercially produced, using 0.002 in. by 0.050 in. tape
and the offset recording and reproducing pole pieces of Fig. 1(5) in which an extended
frequency response and dynamic range are realized at a comparatively low operating
speed. The solid magnetic recording materials, both tape and wire, have the common dis-
advantage that accurate dimensional tolerances, smooth surface conditions, and uni-
formity of heat treatment must be maintained on large quantities of a material that is
inherently very difficult to fabricate.
Coated paper and plastic recording media are applicable to all uses where requirements
on playing time are not excessive and its low remanence can be tolerated. It has been
used in the form of tape, sheets, and disks. The material is cheap to manufacture and
may be cut and spliced by cementing. The material is usually 0.0015 to 0.0025 in. thick.
In contrast to steel wire and tape, when a reel of the material is removed from a machine,
there is little danger of freely uncoiling, a characteristic that is very desirable in the home
recording field. When used with a properly designed ring-type recording-reproduciiig
head a favorable frequency characteristic may be obtained with a comparatively low
operating speed. Output levels are much lower than can be attained with solid wires and
tapes, and care is required in shielding the reproducing head and in the design of reproduc-
ing amplifiers. Although the inherent dynamic range of the coated media is quite large,
thermal and hum noise levels in reproducing equipment may limit the practical dynamic
range.
Certain, special applications of magnetic recording have employed magnetic media in
the form of solid disks or cylinders. Most frequently the recording surface is electroplated
on a non-ferrous backing material.
13-36 ELECTROMECHANICAL-ACOUSTIC DEVICES
MAGNETIC MATERIALS. A carbon-steel recording medium was used in most of
the early equipment because it is commercially available in the form of music wire. It
has very little value in. present-day recording applications. The coercive force is low,
approximately 40 oersteds, and thus self-demagnetization is very pronounced. The
residual induction is approximately 10,000 gausses. Because of demagnetization the short-
wavelength (high-frequency) response from a longitudinal recording is very limited. The
material magnetizes easily from the recording on adjacent turns of the storage spool, and
crosstalk is therefore high. The basic background noise is rather high and is increased
by surface corrosion of the material.
Thirteen per cent chrome steel has been used to a considerable extent in both magnetic
wire and tape recorders because of its resistance to corrosion. This is a ferritic material
depending mostly on the presence of carbon for its magnetic properties. The chromium
is, however, instrumental in obtaining the desired hardness. When properly quenched,
the material has a coercive force of 50-60 oersteds and a residual induction of 7000-
10,000 gausses. A frequency response and dynamic range superior to carbon steel
may be obtained from the material. High operating speeds are required, however, when
an extended frequency range is desired. To prevent formation of chromium oxides, which
are very abrasive, the material is heat treated in an atmosphere free of oxygen.
Nickel-chromium stainless steels such as 18 per cent chromium, 8 per cent nickel have
been used in magnetic wire recorders. This is an austenitic steel which may be hardened
by cold working. A somewhat more uniform product is obtained when the cold-worked
material is then age hardened. After such treatment the coercive force is of the order
of 150 to 350 oersteds with a possible maximum residual induction of 7000 gausses.
Several other magnetic alloys possess properties which make them exceptionally satis-
factory as magnetic recording media. One such material is known as Vicalloy, a workable
permanent-magnet alloy which is heat treated to obtain the desired magnetic properties.
A typical Vicalloy composition is 38 per cent iron, 52 per cent cobalt, and 10 per cent
vanadium. Vicalloy recording tape has been commercially produced with a coercive force
of 225 oersteds and a residual induction of 6000 gausses.
One of the chief disadvantages of the solid magnetic recording media has been the
difficulty of maintaining a uniform recording sensitivity and background-noise level
throughout the entire length of the medium. Recently, an electroplated medium has been
developed in order to correct this disadvantage and at the same time provide a cheaper
recording material. The recording surface consists of a thin layer (approximately 0.0003
in.) of a nickel-cobalt alloy plated on hard brass wire or tape. The magnetic and physical
properties are controlled in the plating process, and subsequent working or heat treatment
is not required. The coercive force is approximately 200 oersteds with a residual induction
of the order of 8000 gausses. A satisfactory frequency range may be obtained from this
material at a comparatively low operating speed.
The use of powdered magnetic materials applied to paper or plastic carriers has recently
received considerable attention in this country. Such a recording medium is comparatively
cheap to manufacture and may be produced with very uniform and stable properties.
Various magnetic materials in powder form are being investigated for properties advan-
tageous to magnetic recording. One such material, black magnetic iron oxide, is com-
mercially available in the required finely divided form. The powdered material is nor-
mally dispersed in a plasticized lacquer and applied to the carrier to a thickness of approxi-
mately 0.0005 in. When the powdered magnetic material is very finely divided and uni-
formly dispersed in the binder very excellent results have been obtained both in frequency
response and background noise. Coercive forces ranging between 100 and 500 oersteds
have been measured. The residual induction is very low, and of the order of a few hundred
gausses. Demagnetization of signals of short wavelengths appears to be less pronounced
in the powdered materials than in solid materials of equal coercive force. Output levels
are very low, and, unless a very wide sound track is used, unusual precautions are required
in the design of reproducing equipment which will take full advantage of the inherent
dynamic range of the medium.
In Germany considerable work has been done on tape in which the magnetic medium
is ferric and ferrous oxide in individual particles about 1 micron in size. This material is
manufactured from precipitated finely divided black magnetic iron oxide by further
oxidization in an agitated drier. The red ferric oxide has the crystal structure of the mag-
netic oxide and is also magnetic. Several types of recording tape have been manufactured
in which the magnetic oxides are either cast on the surface of a plastic carrier such as
cellulose acetate or polyvinyl chloride or are dispersed throughout a tape of polyvinyl
chloride in a 50-50 mixture. It is reported that a frequency response uniform to within
d=2 db from 50 to 10tOOO cps is obtained at a tape speed of 30 in. per sec, the overall noise
level is very low, and the useful life of the recorded tape exceptionally high.
RECORDING INSTRUMENTS 13-37
BIBLIOGRAPHY
V. Poulsen, Ann. d. Pkysik, VoL 3, 754 (Dec. 13, 1900).
V- Poulsen, Electrician, Vol. 46, 208 (Nov. 30, 1900)
L. Bdlstab, E.T.Z., VoL 22, 57 (Jan. 17, 1901)
J. H. West, E.T.Z., VoL 22, 181 (Feb. 21, 1901).
A. Nasarischwily, E.T.Z., Vol. 42, 1068 (Sept. 22, 1921).
W\u* 30ril5|7and Glelm W" Carpenter' U- S- Pat" 1.640.881, appHed for March 26, 1921; issued
C/Stilie, E.T.Z', VoL 51, 449 (March 27, 1930).
E. Meyer, Handbuch der experimental Pkysik, VoL XVII, Chapter 11.
C. N. Hickman, Bell Lab. Rec., VoL 11, 308 (June 1933).
R. F. Mallina, Bell Lab. Rec., VoL 13, 200 (March 1935).
E. Schuller, E.T.Z. , VoL 56, 1219 (Nov. 7, 1935).
H. Lubeck, Akustiche Zeit., VoL 2, 273 (November 1937).
C. N. Hickman, Bell Sys. Tech. J., VoL 16, 165 (April 1937).
S. J. Begun, J. S.M.P.E., VoL 29, 216 (August 1937).
A. E. Barrett and C. J. F. Tweed, J. I.E.E., VoL 82, 265 (March 1938).
D. E. Wooldridge, U. S. Pat. 2,235,132, applied for July 29, 1939; issued March 18, 1941.
M. Camras, U. S. Pat. 2,351,004, applied for Dec. 22, 1941; issued June 13, 1944.
S. J. Begun, Proc. I.R.E., VoL 29, 423 (August 1941).
Marvin Camras, Radio News, Radionics Dept., VoL 1, 3 (November 1943).
Hershel Toomim and David Wildfeuer, Proc. I.R.E., Vol. 32, 664 (November 1944).
L. C. Holmes and D. L. Clark, Electronics, VoL 18, 126 (July 1945).
S. J. Begun, Communications, VoL 26, 31 (April 1946).
D. E. Wooldridge, Trans. A.I.E.E., VoL 65, 343 (June 1946).
C. W. Hansell and others, Dept. of Commerce, Office of the Publication Board, PB 1346.
J. Z. Menard, Dept. of Commerce, Office of the Publication Board, PB 12659.
MECHANICAL RECORDING
AND REPRODUCING OF SOUND
By L. Vieth and H. A. Henning
The requirements for high-fidelity recording and reproduction of sound are (a) that the
whole system, from the point where the sound reaches the pickup device to the point where
it is actually reproduced as sound, shall have a linear relationship between its input and
its output, (6) that the system have a uniform response versus frequency characteristic,
since any complex wave may be resolved into the sum of simple sinusoidal terms, and (c)
that the system have a linear relationship between its phase shift and the frequency im-
pressed upon it and that the phase angle have a value of ±mr at zero frequency where
n — 0, 1, 2, 3, etc. The requirements of individual components may vary from the require-
ments of uniform response versus frequency characteristic (&), but in general the re-
quirements for the system apply to its components.
Most sound recording and reproducing systems and components represent a compromise
between the requirements for high-quality reproduction and the commercial requirements
of size, cost, and general adaptability for a specific use. These compromises have resulted
in a wide range of overall performances. Space limitations prohibit discussion of more
than a few of the typical instruments in commercial use in the mechanical recording and
reproducing of sound.
23. RECORDING INSTRUMENTS
Mechanical recording is used almost exclusively in the present-day phonograph industry,
in electrical transcriptions for broadcast purposes, and in stenographic applications
(dictation machines) and general utility recorders. Most mechanical recording is done on
disks varying in diameter from 6 in. for general utility equipment to 16 in. in broadcast
transcriptions. There are, in addition, several commercial devices in which the recording
medium takes the form of standard motion-picture film base. The materials of which
these media are made are discussed elsewhere. They may be grouped, in general, into two
classes: (a) materials for recording for instantaneous playback; (Z>) materials for recording
for subsequent processing. However, the function of the recording instrument is the same
in all : to transfer to the recording medium, in the form of emboesed or engraved modula-
tions, a counterpart of the voltage impressed on the recorder modified in frequency char-
acteristic in conformance with some preconceived plan of equalization which affords the
optimum use of the recording equipment.
A typical recording instrument used in this work is illustrated by Fig, 1, which shows a
phantom view of a lateral-type recorder (one in which the stylus moves laterally parallel
13-38 EUBCTROMECHAlSriCAL-ACOITSTIC DEVICES
Magnetizing
Winding
Magnet
stylus
f$FiG. 1. Electromechanical Type Recorder
s: _
-*
S £«> c/ig ^g >• cng Q •££ -S
O u11- Bog «C CO ^C (a -1" -1
3 |«J^~-0= » .£= ^ ^gfe
P c; oo^5o "5 oo o 333
.< ~Z^o OO CQO O OO O Q£c/3 OS
FIG. 2. Equivalent Circuits of EJlectromechanical Recorder Shown in Fig. 1
vo Velocity In dl
5 o S <
"^n
N
*-—
*^»
^-
K— 2O
0 50 10O 500 1QOO 5OOO 10,OOO
Frequency in Qyctes per Second
Response TS. Fretniency Characteristio of a Lateral Type Recorder
RECORDING INSTRUMENTS
13-39
to the radius of the disk) designed by Bell Telephone Laboratories*some years ago. The
same general structure has been used in vertical-type recorders (one in which the stylus
moves normal to the face of the disk) . The structure is a mechanical filter whose electrical
equivalent is shown in Fig, 2, in which the current in the second mesh is analogous to the
Fia. 4. Cross-sectional View of Vibrating System and Associated Magnetic Circuit of Western Electric
Co. 1A Feedback Recorder
stylus velocity. Figure 3 shows a typical response versus frequency characteristic of such a
recorder. The loss at the lower frequencies is part of a preconceived equalization plan
which makes the best use of the recording medium by limiting amplitudes in the interest
of record space economy.
The vibratory system of a more modern version of recording instrument is shown in
Fig. 4. This device, also designed at Bell Telephone Laboratories, utilizes the principle
of stabilized feedback to control the stylus velocity and involves an associated amplifier
in which? the recorder becomes an actual transmission element as well as a terminal trans-
ducer. Schematically, the device associated
with an appropriate amplifier may be repre-
sented as shown in Fig. 5. The output volt-
age E<i of the amplifier is supplied to the driv-
ing coil of the recorder, thereby driving the
stylus with a velocity V. Motion of the
stylus in turn generates in a suitable generat-
ing element, such as a small coil moving in a
magnetic field, the voltage E$. This voltage
is returned to the amplifier input through a
control circuit which may be either passive
or active. The voltage available after modt-
fication in the control circuit is designated E^.
The voltages and velocities here referred to are to be considered as having both magnitude
and phase and hence can be represented in complex number notation. Then
», ___ J
FIG. 5. Schematic Representation of an. Elec-
tromechanical Feedback System
= S
(1)
To obtain a simple expression for the relation of the stylus velocity V to the signal
voltage E, let
and
and hence
Et
V
V E*
(3)
(4)
13-40 ELECTROMECHANICAL-ACOUSTIC DEVICES
The product AB thus defines the transmission around the loop formed by the amplifier,
recorder, and feedback control. The value of E4 from this equation can now be substituted
in the relation EI — E + E± to obtain
(5)
which, together with eq. (2), gives
V
1 - AB
E -
(6)
The right-hand side of eq. (6) is the familiar expression for feedback amplifiers in gen-
eral, and the rules for stability, gain, distortion, etc., are equally applicable. In particular,
when AB is very large compared to unity
-B
E (\AB\ » 1)
(7)
which indicates that over the frequency range considered the velocity of the stylus is
independent of the amplifier gain or the efficiency of the recorder. Variations in B,
however, directly affect the performance, and hence, if a fiat frequency response is desired,
B must remain constant. However, since B is the product of the mechanical-electrical
conversion factor E$/V and the control factor EJEz, it will be seen that these factors may
vary as long as their product remains constant. It is a simple matter to maintain the
factor Ez/V constant, and hence a fiat response characteristic depends only upon keeping
the control factor constant.
If eq. (6) is rewritten to include noise and distortion products as well as signal, it becomes
- AB ' 1 - AB ' 1 - AB
(8)
where n and d are the noise and distortion, respectively, introduced in the amplifier and
recorder without feedback. Hence, when AB is large compared to unity, both the noise
and the distortion components are reduced as compared with the corresponding effects
in a non-feedback system.
Variations in the im-
pedance of the recording
medium which act upon
the stylus during cutting
may be regarded as noise
or distortion introduced
in the recorder, and their
effect upon the vibra-
tional velocity is also re-
duced by the above factor.
This is equivalent to a
manifold increase in the
driving-point impedance.
A frequency response
characteristic with and
without feedback on a
typical feedback-type re-
corder is shown in Fig. 6.
The flat frequency re-
sponse characteristic
i- .. j - j. -, ,. . , shown is, of course, of
hmited use m disk recording since the large amplitudes at low frequencies are prohibitive.
However, since the overall characteristic of the device is flat, pre-equalization can be
accomplished flexibly and simply by electrical networks.
RESPONSE IN DECIBELS
JL _ 10 CJ K ,,
O O O O 0 o o
/*•
A-
WITHOUT
FEEDBACK^
/
\
\
/
\
\
f*
/
\
\
/
/
B-wrr
H FEE
)BA
V
^
\
X,
•7
\
10,000 20/>00
20 40 60 100 200 400 1000 2000 4000
FREQUENCY IN CYCLES PER SECOND
FIG. 6. Curves Showing the Stylus Velocity for a Constant Signal In-
put to the Recorder Amplifier System. (A) Without feedback; (5)
with properly controlled feedback.
24. RECORDING AND REPRODUCING MEDIA
Two broad classifications may be made of mechanical recording media: (a) the "wax"
disk intended primarily for subsequent processing and duplication, and (6) the instantan-
eous media disk or otherwise, intended mainly for reproduction directly from the embossed
or engraved master The latter are occasionally used for subsequent processing and dupli-
<*' cylinders are used to some extent in dictating machines as direct playback
EECOEDING AND REPRODUCING MEDIA
13-41
FIG. 7. Western Electric Co. Lateral Recording Styliis
RECORDING DISKS FOR PROCESSING AND DUPLICATION. The shape of the
recording stylus vanes somewhat in commercial practice in the cutting of disks for subse-
quent processing and duplication. In general the cross-section and particularly the curva-
ture of the unmodulated groove are kept within fairly narrow limits. The stylus used on
Western Electric recorders has a tip radius of 0.0021 in. ±0.0001 in. Its contour is illus-
trated in^ Fig. 7. The disposition of grooves and land between grooves is a matter of
compromise between playing time and signal-to-noise ratio and other factors. For lateral
recording the groove pitch is usually between 0.007 and 0.010 in. as illustrated by Fig. 7.
The maximum safe amplitude at any point on the groove will depend upon the amplitude
and phase of the sound recorded on the adjacent grooves. For a groove situated between
two unmodulated grooves, the maximum amplitude for the condition pictured in Fig. 7
will be nearly 0.004 in. The maximum amplitude for two adjacent grooves of equal ampli-
tude and 180° out of phase with each other will be slightly less than 0.002 in. The space
between grooves may be compressed, in vertically cut recordings, to increase the playing
time of a record with less sacrifice
in recording level than for lateral
recording.
In cutting, the "wax'* (more
correctly a metallic soap) must be
leveled on the recording machine
with reasonable care, and the
stylus must be sharp and so ground
that the cut will be very clean. As
it is cut the wax shaving is removed
by air suction. The operator is
aided in maintaining the correct
depth of cut by a so-called advance
ball. Commonly an advance ball
is a ball-shaped sapphire mounted
in an adjustable holder which is in
turn fastened to the recorder. The
advance ball rides lightly over the
wax close to the stylus and serves to maintain uniform depth of cut in spite of small in-
accuracies of leveling of the "wax" or deviation from planeness. The advance ball is
adjusted relative to the stylus by observing the cut with a calibrated microscope.
In commercial cutting, for processing, both solid and flowed waxes are popular. Solid
disks are shaved with a sapphire knife to a highly polished surface on a sturdy high-speed
turntable. After recording and processing the disk is reshaved and recut until it becomes
too thin to be used with safety. The flowed disk is a thin layer of wax flowed onto a metal
surface. The wax layer is cut once and discarded, the metal backing being reused indefi-
nitely. Such a recording medium is extremely smooth, homogeneous, and free from
mechanical strains incidental to shaving the "waxes" by the older method.
DUPLICATION OF DISK RECORDS. The surface of the wax, after being engraved,
is -rendered electrically conducting. This can be done in a number of ways, such as dusting
with graphite and bronze or other electrically conducting powders, by the chemical pre-
cipitation, of silver, .or by sputtering a suitable material such as gold or silver in a cathode
sputtering chamber.
The wax is then electroplated with copper, sometimes to a thickness of about x/32 in-»
or sometimes only to a thickness of a few thousandths of an inch and then backed up by a
thicker metal plate of suitable material. This electrodeposited plate is then a negative of
the wax and is called a "master." From this negative or master, positive copies may be
made. In commercial practice the copies or records are usually pressed of some thermo-
plastic material. If the sound reproduction from a few records carefully pressed from a
master is satisfactory, duplicate stampers are produced in order that the master may be
preserved. These duplicate stampers are used for pressing or molding the commercial
release records.
From the master one or more "mother" plates are made by eJectrodepodition. These
mothers are positives and serve as the forms on which the final matrices or stampers are
deposited. One of the important problems in this process is the treating of the metal
surfaces of the masters and mothers so as to permit subsequent separation. The problem
is to produce a surface which will still be conducting, but which is not "clean'*; i.e., the
deposited metal must not be in sufficiently intimate contact with the metal of the mold
to cause permanent adherence. This may be done by either of two methods: (a) by the
application of a thin "mechanical" layer of some substance such as grease, graphite, etc.,
or (&) by a chemical film usually produced by treating the previously cleaned metal surface
13-42 ELECTROMECHANICAL-ACOUSTIC DEVICES
with some chemical that will react with the metal and produce an insoluble compound.
Typical substances for the purpose are soluble sulfides such as sodium sulfide (Na2S) or
the yellow "polysulfide" (Na2Sa:). These will react with the metal to form films of the
corresponding sulfides. Frequently the phonograph industry has employed a film of
silver iodide, formed by first treating the copper surface with a silver cyanide solution.
The solution is either poured over the previously cleaned surface or mixed with an inert
substance such as whiting or calcium carbonate (CaCOs) to form a paste which is rubbed
over the copper. A thin film is thus deposited by immersion. The film is then treated
with a weak iodine solution. The iodine solution acts upon the silver to form a thin film
of silver iodide upon which the copper can then be deposited and subsequently separated.
Numerous other methods are employed in the industry.
Until recently the records themselves were molded of a thermoplastic mixture of shellac
and earth fillers and were generally played with steel needles. The fillers were purposely
made somewhat abrasive in order to grind the needle point to fit the groove since the
needles were not usually accurately shaped to a suitable contour. The pressures at
the needle point of a typical needle, before being ground to shape, are extremely high, and
record wear under this condition is serious. In more recent years, reproducers of lower
mechanical impedance have become available, which require much lower pressures. Accu-
rately contoured permanent reproducing points provide further relief by reducing vibra-
tory mass and maintaining a definite small raolius of curvature. Any abrasive in the
records adds to the background noise, hence homogeneous, non-abrasive records such as
those made of cellulose acetate or vinylite are coming to be used. Such materials are, in
fact, used almost universally in transcription recordings for broadcast purposes.
Records of the older shellac mixtures or of some of the more recently developed plastic
materials are made in about the same manner, although the time, temperature, and pres-
sure cycles may differ widely. The material to be molded is usually heated to a suitable
softening temperature (of the order of 300 deg fahr) either on an auxiliary hot plate or in
the record press itself in which the stampers are mounted. The stampers are commonly
mounted in the press on platens which are heated and then cooled according to some pre-
determined cycle. The material may be further heated in the press at a suitable tempera-
ture before the pressure of the press is applied upon it. The pressure applied is of the
order of 2000 Ib per sq in. for many plastic materials. This pressure is maintained while
the platens are cooled for a suitable time, after which the press is opened and the record
removed.
INSTANTANEOUS PLAYBACK DISKS. This term covers a multitude of plastics
and metals which lend themselves to easy engraving or embossing. A few will be discussed.
In the higher-quality field of instantaneous recording media the 12 in. and 16 in. lacquer-
coated disks of glass or metal are most common. A variety of materials may be com-
pounded with cellulose nitrate to form a lacquer that is easily engraved. These coatings
are approximately 0.010 in. thick and cut cleanly with a recording stylus similar to that
used for cutting "wax," although it is general practice to somewhat dull the cutting edge
to a radius of the order of 0.0003 in. The shaving may be directed toward the center and
collected about the center pin of the disk or it may be removed by suction apparatus.
Disks of this kind are sometimes used as masters for subsequent processing and duplica-
tion in the same manner as described for wax disks. When the disks are used for instan-
taneous playback, the elastic properties of the recording material seriously affect the re-
sponse characteristic. High-frequency losses, particularly at low linear velocities, are
very severe and are not too satisfactorily relieved by predistortion in recording. Depend-
ing upon the type of reproducer used on these disks, they may be good for from one to
fifty playings.
In the general utility field recording disks are most commonly made of vinylite or
vinylchloride. Gelatin and soft metals such as aluminum are also used. These materials,
in general, are not suitable for engraving, and in most applications an embossing stylus
is used which rubs a shallow groove into the recording material, modulating the groove in
accordance with the signal impressed on the recorder. The contour of such styli varies
widely. Grooves so rubbed are about 0.001 in. deep and the maximum amplitude rarely
exceeds 0.001 in. Signal-to-noise ratios are relatively low. These applications are defi-
nitely not high quality in their present state of development, emphasis being placed on
obtaining good articulation. Useful playing life is uncertain. Extremely light reproducers
and soft reproducing styli are required if more than a few playings are anticipated. Disks
in general do not exceed 6 or 8 in. in diameter.
RECORDING MEDIA OTHER THAN DISK. Although the recording medium on
most general-utility recording machines takes the form of a disc, two exceptions worthy
of Etote are made. The first of these is film on which the recorded grooves are embossed
in iteiical pattern on an endless loop of standard 35-mm safety motion-picture film base
REPRODUCING INSTRUMENTS
13-43
(Amertype Recordgraph) . The other exception is the well-known wax cylinder which
approximates in its consistency the wax disk used in recordings for processing. Here a
helix is cut in the cylinder to be erased for subsequent reuse after playing (Dictaphone and
Hidiphone) .
A unique combination of mechanical recording and optical reproduction is found in the
Phinpps-Miller system, in which a wide-angle stylus cuts an extremely shallow groove
through the darkened emulsion of a photographic film. The thin emulsion is therefore
cut away in varying widths so that the transparent body of the film presents a pattern
similar to that of variable area sound-on-film recording. Reproduction is accomplished
optically in a similar manner to ordinary sound on film.
25. REPRODUCING INSTRUMENTS
The function of the reproducer in a mechanical recording system is to transform into
electrical energy the modulations of the recorded disk or duplicate thereof. Since the
inception of so-called "electrical recording" in contrast to the older method of acoustical
recording, magnetic-type reproducers have played an important part. Such reproducers
have taken a variety of forms, but in general an armature is rigidly attached to a stylus
holder. The armature, moving in a magnetic field, generates a voltage in associated coils.
Typical examples of such structures are illus-
trated in Figs. 8 and 9. Both these devices ^"" — " ~""-\ Magnet
and others of the same vintage are lateral-type
reproducers and are intended for use with a re-
placeable steel stylus or needle. To provide
sufficient rigidity against flexing, such styli in
themselves are quite heavy, and their mass plus
that of associated driving elements produces a
FIG. 8. Early Type Western Electric Co. Oil-damped
Lateral Reproducer
FIG. 9. Early Type RCA Victor Re-
producer
high driving-point impedance with corresponding record wear and distortion. In general,
the same applies also to the fitted jewel styli used in conventional-type lateral reproducers,
In reproducing vertical recordings the driving force is in direct line with the stylus axis
and flexural rigidity is not so important a requirement. The mass of the stylus aad asso-
ciated vibratory system can therefore be kept comparatively small, thus redseang the
driving-point impedance so that record wear is greatly reduced. Vertical reproducers m
general have been built around the moving-coil principle and invariably are associ^ed
with a jeweled (diamond or sapphire) stylus that has been polished to fit t&e recorded
groove accurately. . ,
One of the more common of reproducers is the piezoelectric crystal type, in wiucn a
Rochelle salt crystal element is secured to a stylus holder at one end and anchored at tbe
other. Stylus movement causes a flexing of the crystal element, which produces a voltage.
In general that type of reproducer is of fairly high driving-point impedance, although some
•of the higher-quality devices provide a distinct improvement in this respect, figure 1U
.shows a cross-section view of the "cartridge" of a typical crystal-type reproducer. _ _
An interesting reproducer which serves to illustrate at once the moving-coil principle
13-44 ELECTROMECHANICAL-ACOUSTIC DEVICES
CRYSTAL
ELEMENT
TORSIONAL
f DRIVE WIRE
METAL
BEARINGS
\
CRYSTAL
MOUNTING PADS
BEARING SUPPORTS
(RUBBER) STYLUS
Pro. 10. Brush Development Co. PL-20 Crystal Reproducer
as applied to both vertical- and lateral-type reproducers is the Western Electric 9A repro-
ducer, a phantom view of which is shown in Fig. 11, This is a universal reproducer, that
is, one which will reproduce either vertical or lateral recordings by changing the electrical
pFia. 11. Western Electric Co. 9A Universal Reproducer
relationship of the two voltage generating coils. Figure 12 shows the response charac-
teristic of this device on both types of recordings.
Jeweled styli have become commonplace in many makes of reproducers. Their contours
<o-65|
100 200 SCO 1000 2000 50OO 10,OOO 20,000
FREQUENCY IN CYCLES PER SECOND
PIG." 12. Response vs. Frequency Characteristic of Typical 9A Repro-
ducer
vary, but in general the
radius of the spherical
tip is held to between
0.002 and 0.003 in. The
larger tip radii, though
permissible and even de-
sirable in certain types.
of lateral reproducers, in.
general induce serious.
distortion products.
They do, of course, re-
duce wear on the record.
SOURCES OF DISTORTION 13-45
26. SOURCES OF DISTORTION
RECORDING. In all recording instruments sources of distortion common to most
electromechanical transducers are present. Magnetic elements do not always behave
linearly, and mechanical elements are frequently free to respond in modes other than the
desired one. In general, however, distortion due to these effects can be minimised by good
engineering and design. Recorders intended for use in a variety of recording media do
not always meet the same impedance at the cutting point. Not only does this impedance
vary from one medium to another; it may vary also with depth of cut in a given medium.
It has been customary, therefore, to keep the driving-point impedance sufficiently high
so that the recording medium has little or no effect on the recorder characteristics. The
maximum force on the stylus in cutting is developed by the reaction of the record material
to be cut away. This force is normal to the motion of the stylus, and yielding by the stylus
arm in this direction occurs in the neighborhood of the stylus-arm resonance frequency.
This motion is introduced on the time axis of the recording, and intermodulation with
other frequencies results.
A less important source of distortion which intrudes also on the smoothness of cutting
is the design of the stylus. The dimensions of the stylus, like so many other elements in
recording systems, are a compromise between many factors, including linear velocity and
recording amplitude. In order to provide adequate ruggedness at the tip, a short bevel
at a rather blunt angle is provided, as is shown in Fig. 7. The slope of this bevel marks
the maximum slope that can be tolerated in vertical recording without having the heel of
the stylus abrade the modulated groove. The corresponding critical angle in lateral
recording is approximately 45°, which means that the maximum recorded vibratory
velocity must never be more than the linear velocity of the record.
PROCESSING AND DUPLICATION. Although electrodeposition is one of the
most accurate methods known for duplicating a surface, several sources of distortion
present themselves. Plating on the face of copper stampers of abrasion-resistant chro-
mium or other metallic finish has a finite thickness sometimes comparable with the modu-
lations of the grooves. When this process is repeated a number of times, as is common
commercial practice, high frequencies are all but obliterated. Stampers are occasionally
burled before or after plating. This, of course, very rapidly erases, in a random manner,
much of the higher frequencies.
REPRODUCING. The distortions introduced in recording and processing can be
minimized by good design and careful handling. In the interest of commercial expediency
these factors are sometimes overlooked. In reproducers, however, there are in the present
state of the art several distortion-producing factors which might be characterized as in-
herent. The first of these, termed "tracing" distortion, is due to the fact that the re-
producer stylus has finite size. The curve traced by the center of a spherical-tip stylus in
tracing a sinusoidally modulated groove is not sinusoidal. This effect increases rapidly
as the minimum radius of curvature of the recorded wave approaches the radius of the
stylus tip. Practical considerations prevent relief by the simple expedient of making the
stylus radius smaller.
The TYnm'rnum radius of curvature of a sine-wave groove is given by
where R = niinimurn radius of curvature (inches), V — linear speed of groove (feet per
minute), A = amplitude (inches), and / = frequency (cycles per second). The linear
speed V of a 12-in. record at the standard turntable speed for phonographs, 78.26 rpm,
varies between 1.3 and 3.8 ft per sec. At the standard broadcast transcription speed of
33.33 rpm the linear speed of a 16-in. record varies between 1.2 and 2.4 ft per sec. At liigh
frequencies, therefore, for even extremely small amplitudes the radius of curvature of
the modulated groove may be comparable with that of the stylus attempting to trace it.
Fortunately, the distribution of energy in speech and music spectra is such as to alleviate
this situation. However, hi the interest of noise reduction and standardization of recording
techniques it is an, accepted procedure to accentuate high frequencies in recording with
corresponding attenuations in reproduction.
In lateral reproduction the problem is further complicated by what has been described
as "pinch*' effect; i.e., since conventional lateral reproducers have no vertical compliance
the stylus "pinches" between the walls of the grooves when the linear velocity drops below
a certain point. This phenomenon results from the fact that the cutting surface of the
recording stylus is always perpendicular to the unmodulated groove. A constriction.
therefore results in the width of those portions of a modulated groove which are at an
angle to the direction of the unmodulated groove, i.e., at all portions of the modulated
13-46 ELECTKOMECHANICAL-ACOUSTIC DEVICES
grooves except the maxima and minima and points of inflection. Some relief is afforded
by providing appropriate vertical compliance in lateral reproducers, and in such repro-
ducers it is advantageous to use an oversize reproducing stylus which never rides on the
groove bottom but is always positively driven by the side walls. It has been shown that
in this way even harmonics can be eliminated from "tracing" distortion.
Another source of distortion in reproduction is due to "tracking error." Tracking error
may be defined as the angle between the vibration axis of the mechanical system and the
tangent to the groove being reproduced. This angle results from the conventional device
of pivoting the reproducer arm at a fixed point. The aforementioned vibration axis can
therefore be truly tangent to the record groove at only one radius. In lateral reproduction
when the tracking error is large a sinusoidal wave is not traced sinusoidally. This effect
is minimized in lateral reproduction by the well-known device of an offset reproducer
head or by making the pivoted reproducer arm very long. Mechanisms which keep the
reproducer tangent at all times are employed in a few reproducing devices, eliminating
this source of distortion entirely. In vertical reproduction, distortion due to tracking
error is negligible.
The characteristics of the medium of which disks are made contribute to the distortion
in reproduction. The modulated groove which drives a reproducer stylus has a finite
impedance which at some frequencies may be comparable with or less than the stylus-
point impedance. With modern high-quality reproducers the compliance of the record
material resonates with the vibratory mass of the reproducer, frequently producing a
peaked response at some high frequency, above which the response very rapidly declines.
The most outstanding examples of the effect of record characteristics on response are found
in the instantaneous types of playback disk. The materials of which these disks are made
have a high compliance. The losses at high frequencies, particularly at low record veloci-
ties, are serious even with the best of commercial reproducers. Compensation for such
losses is difficult because the magnitude of the loss varies widely, increasing as the linear
velocity decreases.
BIBLIOGRAPHY
T. A. Edison, U. S. Pat. 200,521.
H. M. Stoller, J. S.M.P.E., 1928.
O. J. Zobel, B.S.T.J., 1928.
S. P. Mead, B.S.TJ., 1928.
H. A. Frederick, J. A.S.A., 1931.
E. C. Wente and A. L. Thuras, J. A.S.A., 1931.
W. C. Jones and L. W. Giles, J. S.M.P.B., 1931.
W. C. Jones, J. S.M.P.E., 1931.
E. G. Wente, Phys. Rev., 1922.
H. F. Olsen, J. A.S.A., 1931.
H, C. Harrison and P. B. Flanders, B.S.T.J., 1932.
H. D. Arnold and I. B. Grandall, Phys. Reo.t 1917.
Tucker and Paris, Phil. Trans. Roy. Soc., 1921.
A. V. Hippel, Ann. d. Physik, 1925.
W. Spaeth, Zeit. tech. Phys., 1925.
U. S. Patent 1,634,210, 1927.
Olson and Massa, Applied Acoustics. P. Blakiston's Son & Co., Philadelphia.
J. P. Maxfield and H. C. Harrison, Trans. A.I.E.E., 1926.
C. F. Eyring, J. A.S.A., 1930, 1931; J. Soc. Mot. Pict. Eng., 1930.
H. L. Hanson, J. S.M.P.E., 1930.
F. L. Hunt, J. A.S.A., 1931.
W. A. MacNair, J. A.S.A., 1930; Proc. I.R.E., 1931.
J. C. Steinberg, J. A.S.A., 1929.
W. C. Sabine, Collected Papers on Acoustics.
L. J. Sivian, H. E. Dunn, and S. D. White, J.A.S.A., 1931.
J. P. Maxfield, J. S.M.P.E., 1930.
-L. Cowan, Recording Sound for Motion Pictures. McGraw-Hill, Chapters 4 16
E. O. Scriven, J. S.M.P.E., 1928; B.S.T.J., 1934,
W. P. Button and S. Read, Jr., J. S.M.P.E., 1931.
S. Read, Jr., J. S.M.P.E., 1933.
R. A. Miller and H. Pfannenstiehl, J". S.MJP.E., 1932.
H. A. Frederick, J. S.M.P.E., 1928, 1932.
P. Wilson and G. W. Webb, Modem Gramophones and Electric Reproducers. Cassell & Co. (1929).
S. r. Williams, J. Franklin Inst., 1926.
H. A. Frederick and H. C. Harrison, Trans. AJ,E.E.r 1933.
A. Gizntherschuze, Zeit. f. Phys., 1926.
H. F. Fnith, B.S.T.J., 1932.
W. Blum and G. B. Hogaboom, Principles of Electroplating and Electro forming. McGraw-Hill.
F. C. Barfeon, J. S.M.P.E.V 1934.
L. F. Rahm, Plastic Molding, McGraw-Hill (1933).
K W. Kellogg, Trans. AJ.E.E., 1927.
J. P. MaxfieM, U. S. Pat. RE 18,228.
B. Nesper, Nimm Schallplatten seiner auf. Franckh'sche Verlagshandlung, Stuttgart.
U» fc>» .tut* 1,7 54,935 (.1930).
B. a Pat. 1,421,045 (1922).
AvCL Kefev J. A.S.A., VoL 8 (1937).
PHOTOGRAPHIC SOUND RECORDING
13-47
A. C. Keller, J. S.M.P.E., 1937.
M. J. DiToro, J. S.M.P.E., Nov. 1937.
B. Olney, Electronics, November 1937.
L. Vieth and C. F. Wiebusch, J. S.M.P.E., January 1938.
J. A. Pierce and F. L. Hunt, J. S.M.P.E., August 1938.
H. A. Henning, Bett Lab. Rec.> October 1940.
W. D, Lewis and F. L. Hunt, J. A.S.A., January 1941.
L. Fleming, J. A.S.A., January 1941.
B. B. Bauer, Electronics, March 1945.
B. B. Bauer, J. A.S.A., April 1945.
H. E. Boys, J. S.M.P.E., June 1945.
W. S. Bachman, Electronic Industries, July 1945.
PHOTOGRAPHIC SOUND RECORDING
By C. R, Keith
The photographic method of sound recording finds its greatest field in sound pictures,
the sound record being usually on the same film as the picture or at times on a separate
film operating synchron-
ously with the picture film.
Film records are particu-
larly adapted to sound pic-
tures since these films are
usually made from numer-
ous short "takes" which are
edited and then spliced to-
gether. The sound and
picture are usually photo-
graphed on separate films,
except for newsreel record-
ing where the sound and
picture are commonly taken
on the same film. Usually
music and sound effects are
recorded separately from
the dialog; the various
sound tracks are then re-
recorded in synchronism
with the finally cut picture
film, to make a sound nega-
tive which is used for makT
ing release prints.
Two types of sound-on-
film records are in common
use today. One is the vari-
able-density type — a series
of striated bands as shown
in Fig. 1 (a)-(d). The other
is the variable-area type
shown in Fig. 1 (e)-(i) — a
serrated band with its
toothlike projections. Both
place the record on a narrow
strip of the film at one side
of the picture as in the
sketch of a composite print
with a variable-density
sound track (Fig. 2). As
the sound track must be
played at uniform speed
while the picture progresses
with intermittent motion,
it is displaced forward along
the film 15 in. from the
FIG. 1. Types of Sound Tracks
corresponding picture, so that the momentary difference in film velocity can be taken up
13-48 ELECTROMECHANICAL-ACOUSTIC DEVICES
-t-0.100 In.
by a free loop. Both types of sound track can be reproduced in the same machine with-
out any change in the machine or in the electrical equipment.
The most commonly used sound tracks are illustrated in Fig. 1. Films exhibited in
theaters ordinarily have single 100-mil tracks such as (a), (b), (e), (/), or (g). Original
sound records are often made with 100-mil pushpull tracks
such as (c) or (i) or more commonly, when the sound is
recorded on a film separate from the picture film, with a
200-mil pushpull track such as (d) or (h) .
There are many methods of producing such film sound
tracks: the light- valve method (Western Electric), the reflect-
ing-galvanometer method (RCA), the flashing-lamp method
(Fox-Case), the Kerr cell (Klangfilm\ and many variations of
these methods. The flashing lamp and the Kerr cell are used
only for variable-density tracks, but the light valve and the
reflecting galvanometer may be used for either variable-density
or variable-area tracks.
27. LIGHT-VALVE RECORDING SYSTEM
In the light-valve system the light from an incandescent
source is made to fall on a light valve, Fig. 3, formed of two
strips of Duralumin 0.0005 in. thick by 0.006 in. wide spaced
0.001 in. apart. These are placed in a magnetic field and carry
the speech currents. Since the two ribbons carry current in
opposite directions they move together or apart as the current
varies. In commercial practice the ribbons are tuned or reso-
nated to about 9500 CRS. The response in the frequency range
near resonance depends on the damping, and in early types of
light valves the response at resonance was 20 to 25 db higher than at low frequencies.
This variation in response can be reduced to 1 or 2 db by using a feedback circuit in which
signal voltage across the light-valve ribbons is amplified and applied to the valve input
in opposite phase. However, the more recent light valves have sufficiently high flux den-
sity (30,000 gausses) so that the resonance peak is only about 6 db. Additional damp-
ing is obtained by passive networks in the valve input circuit, so that the resonance peak
may be reduced to about 1 db. These measures also almost entirely eliminate extraneous
vibrations of the light-valve ribbons when excited by steep transients.
In early types of light valves both ribbons were in the same plane so that it was possible
for them to strike each other when caused to vibrate at large amplitudes, thereby increasing
the normal overload distortion. This difficulty is avoided in later types by mounting the
two ribbons in parallel planes separated by about the thickness of one ribbon. In addition
to preventing distortion due to ribbons striking each other, this "biplanar" construction re-
duces the possibility of damage to ribbons through overmodulation.
When the light-valve ribbons are focused directly on the moving film the exposure at
high frequencies does not correspond to the motion of the ribbons if the velocity of either
edge of the image is comparable to that of the film. The exposure given to the film is
H Scanning
-H H-Beam
0.084 In.
FIG. 2. Position of Sound
Track on 35-mm Film
Lamp
Ught Vate
FIG. 3. Optical Schematic of Typical Light-valve Recording System
Objective
Lens
elm
determined by the time required for any point on the film to pass through the image of
the light-valve slit; in other words, the exposure (to a first approximation) is the product
of time and intensity. If the frequency being recorded is low, so that the velocity of the
ribbons is small compared with that of the film, the variations in film exposure will accu-
rately correspond to the light-valve modulation. As the frequency becomes higher, how-
ever, tke velocity of the ribbons increases, being substantially proportional to frequency
LIGHT-VALVE RECORDING SYSTEM
13-49
for constant electrical power input to the light valve, until at the highest audio frequencies
the ribbon- velocity effect may become important. For a sine-wave signal just sufficient
to fully modulate a two-ribbon valve spaced to 0.001 in., the peak ribbon velocity becomes
equal to the film velocity at about 6000 cycles. This results in a loss of high-frequency
response which also varies with the average ribbon spacing. Consequently when a high-
frequency wave is superposed on a low-frequency wave, the high-frequency response
varies during each cycle of the low frequency.
Distortion of this type is not indicated by harmonic measurements since it occurs
mainly at frequencies whose harmonics would be greatly attenuated by other elements
in the system, such as the width of the reproducing slit. Such distortion can, however,
be detected by "intermodulation" tests in which two frequencies are recorded simultan-
eously (one high and one low) and the variation in high-frequency response measured.
In usual practice the amplitude of the low frequency (60 cycles) is four times that of the
high frequency (7000 cycles) . The reproduced wave is passed through a high-pass filter,
eliminating the 60-cycle component. When this wave is rectified a new set of low fre-
quencies (60, 120, 180. . . cycles) is produced, owing to the presence of distortion frequen-
cies in the high-frequency wave. The average amplitude of this new low-frequency wave
is a convenient measure of the distortion. In a suitably designed light- valve modulator
the intermodulation distortion may be reduced to 4 per cent or less, corresponding to
approximately 1 per cent harmonic distortion as measured in a system in which distortion
and transmission do not vary with frequency. This is accomplished by reducing the
effective image width to 0.00025 in. or less, usually by means of a short-focus cylindrical
lens placed close to the film surface.
NOISE-REDUCTION SYSTEM. A noise-reduction system is commonly used in film
recording in order to lower the level of background noise when it is not masked by rela-
tively loud sounds. This system is based on the fact that in a variable-density sound
track the background noise output from a light print is greater than that from a dark
print when reproduced with the same gain setting of the amplifier. However, when a
print is made darker by merely increasing the exposure in the printer, both the ground
noise and the wanted sound are reduced in approximately the same ratio so that no im-
provement in the signal-to-noise ratio results. The desired result is obtained by reducing
the average exposure of the negative during periods of low modulation without reducing
the amount of light modulated by the signal.
In the Western Electric system of noiseless recording the mean spacing of the light-
valve ribbons is made to vary so that as modulation is impressed on the valve the mean
spacing increases sufficiently to accommodate the increasing input. The spacing between
light-valve strings is mechanically adjusted to 0.001 in., and a source of direct current is
connected to the strings sufficient to reduce the spacing to 0.0003 in. (for 10-db noise
reduction) . In addition to this fixed bias a varying bias proportional to the envelope of
the signal wave increases the ribbon spacing as the signal current increases. The lower
average exposure of the negative during periods of low signal levels produces a positive
with relatively high average density during such periods. The ground noise is thereby
reduced when the signal is low, but, since the valve modulation due to the signal is un-
changed, the effective signal-to-noise ratio is increased.
Main
Ampli-
fier
£ S.
l-l [f
Ampli-
fier
Recti-
fier
Timing
RIter
Modu-
lator
Ampli-
fier
Recti-
fier
Biter
FIG. 4. Block Schematic of Noise-reduction System
A block schematic of a typical noise-reduction circuit is shown in Fig. 4. The timing
filter not only serves to remove audible frequencies from the rectified signal but also shapes
the bias wave so that, for rapidly fluctuating signals such as speech, the valve spacing
increases at about the same rate as the signal increases, but the spacing decreases at a
considerably slower rate. The oscillator, modulator, second amplifier, and rectifier merely
form a convenient means of amplifying the fixed and variable bias currents.
13-50 ELECTROMECHANICAL-ACOUSTIC DEVICES
28. REFLECTING-GALVANOMETER RECORDING SYSTEM
The refiecting-galvanometer method, commonly used for producing'variable-area sound
tracks, utilizes a recording device that operates on the principle of the mirror oscillograph.
Light is reflected from the oscillating mirror of the recorder and is passed through a
narrow slit onto the film. The resulting sound track has constant density but variable
(«) CO
FIG. 5. (a) Optical Schematic of Typical Galvanometer Recording System, (b) Recording Gal
eter. (c) Armature Damping in Recording Galvanometer, (d) (e) (/) Typical Mask and Shu1
rangements Used in Galvanometer Recording System.
ivanom-
itter Ar-
width. A widely used type of light modulator accomplishes this by the use of a triangular
beam of light which is caused to move at right angles to the axis of the slit by the recording
galvanometer, so that, as it vibrates, the length of the illnTnj.Ti.ed portion of the slit varies.
The RCA variable-width light modulator, Fig. 5 (a), consists essentially of an incan-
descent lamp, a system of lenses to direct the light, an aperture and slit to limit the light,
FLASHING-LAMP, KERR CELL RECORDING SYSTEMS 13-51
and a reflecting-mirror galvanometer to modulate the light. An image of filament A is
formed at the galvanometer mirror F by the combination of lenses B and E. The aper-
ture C, shown as the shaded area in Fig. 5(d)T limits the light projected to the galvanometer
mirror. Lens E forms an image of aperture <? on slit H. Vibration of the galvanometer
mirror moves this light beam back and forth across the slit so that the length of the illum-
inated portion of the slit is proportional to the angular deflection of the mirror. A reduced
image of the slit is formed on the film K by objective lens J.
^ Ground noise is reduced in this modulator by cutting off the light from the ends of the
slit during periods of low modulation. The two magnetically operated shutter vanes D
are used for this purpose, producing the varying black margins shown, for example, in
Fig. l(g). Current for operating the noise-reduction shutters is derived from the signal
and is proportional to the envelope of the signal wave. During periods of no modulation
the clear area is reduced to a width of about 0.002 in.
Other common accessories in this modulator are a visual monitor system and an ultra-
violet filter. The visual monitor is provided by forming an image of one edge of the aper-
ture C on a monitor card. Vibration of the galvanometer mirror causes the image to
lengthen in proportion to the mirror deflection. By means of suitably spaced lines on the
card the operator is enabled to judge when the galvanometer deflection reaches the
maximum allowable without exceeding the sound-track width (0.076 in.) that can be
scanned by the slit in the reproducing machine. The ultraviolet filter I restricts the film
exposure to a narrow band of wavelengths in the neighborhood of 3650 A, thereby reducing
image spread due to scattering of light in the film emulsion. Recent fine-grain films have
also contributed to improvement in image quality.
The recording galvanometer, Fig. 5(6)r consists of a pair of permanent magnets, pole
pieces, balanced armature A, signal and bias coils C, mirror support, and mirror Af. A
pair of phosphor-bronze springs hold a groove ia the ribbon support against a knife edge
on the end of the armature. Current through either the signal or biasing coils polarizes
the armature, causing it to be attracted to the pole piece of opposite polarity and by its
lateral motion rotating the mirror support and mirror.
One of the serious problems in electromechanical apparatus is the provision of suitable
damping. Oil damping, although widely used in oscillograph galvanometers, has a
number of objections, among which are the change of viscosity with temperature, relatively
large mass required for the damping obtained, and difficulty of avoiding leakage. The
damping in this galvanometer is obtained by utilizing the properties of tungsten-loaded
rubber so mounted that damping is obtained in the frequency range near armature reso-
nance, but without affecting the low-frequency response of the galvanometer. As shown,
in Fig. 5(c), two small pieces of tungsten-loaded rubber R are cemented to the sides of
the armature A, and a bronze yoke presses against their outer faces. At low frequencies
the yoke and pads move with the armature, but at high frequencies the inertia of the yoke
causes it to tend to stand still while the armature vibrates inside it, compressing the rubber
and damping the peak.
Other types of sound tracks can. be made with the same modulator by means of masks
of other shapes. For example a class A pushpull variable-width tra^k may be made with
the mask in Fig. 5 (e) . Class B pushpull variable-width tracks may be made with the mask
shown in Fig. 5(/). Variable-density tracks can also be made by a modificatJoa of this
modulator in which the uniformly illuminated triangles are replaced by a peoumbra
designed to give a linear gradation of light intensity. The galvanometer mirror causes
this penumbra to move across the fixed slit, varying the light transmitted to the film in
proportion to the mirror deflection.
29. FLASHING-LAMP AND KERR CELL RECORDING SYSTEMS
Although not widely used at the present time, the flashing-lamp method of recording
has the advantage of extreme simplicity- The gaseous discharge is concentrated in. a
relatively small area and so designed that the current is proportional to the signal voltage.
An early type of flashing lamp, called Aeolight, is a two-element tube containing an inert
gas such as helium. One of the elements is of nickel; the other is coated with barium and
strontium oxides. When, sufficient voltage is applied 1,0 the electrodes, ioniEation takes
place and a concentrated glow appears at the cathode. The intensity of tfee light so pro-
duced increases in proportion to the increase in applied voltage. la operation, sufficient
polarizing voltage is applied to the tube to give the required average exposure of ^ the
negative, and sound voltages are superposed on this polarizing voltage. Since the light
output is comparatively low, the lamp is usually arranged for direct iHiimination of the
£lm rather than by means of the usual lens system. A fixed slit 0.0008 in. by 0,100 in.,
13-52 ELECTKOMECHANICAL-ACOTJSTIC DEVICES
made by engraving the silvered surface of a small quartz block, is located within less than
0.001 in. of the film. The low light intensity obtained from flashing-lamp light modulators
results in a very low value of negative exposure and is in the region known as the "toe"
of the H and D curve. Prints made from these negatives must be printed on the "toe"
of the positive H and D curve in order to minimize distortion. Consequently the per-
missible modulation ratio is reduced and the volume range is less than for the fully exposed
type of record.
Another relatively low-intensity light modulator utilizes the Kerr electro-optical effect.
A glass cell containing nitrobenzol is placed between two Nicol prisms, and an electrostatic
field is applied to electrodes on either side of the cell. Light from an incandescent lamp is
plane polarized by the first Nicol prisrn, and the second prism is so arranged that, when no
polarizing voltage is applied to the cell electrodes, no light is transmitted. Since the plane
of polarization of light transmitted through the cell is rotated as the polarizing voltage is
increased, the transmitted light also is increased. However, the relation between trans-
mitted light and applied voltage is not linear and introduces appreciable distortion at
high modulation.
30. SOUND-ON-FILM REPRODUCING SYSTEMS
In the reproduction of either of the two normal types of single sound tracks, i.e., var-
iable-density or variable-area, the light from an incandescent filament is made to fall on a
fixed slit which is imaged on
Slit the ^ as a line of
Condenser
Lens
lUght
Source
Film/
Plane
) The "motion picture" type of optical system
Condenser
Objective Lens
Film./
Plane
The "stereoptlcon*1 type of optical system
FIG. 6. Typical Film Reproducer Optical Systems
common optical systems are
shown in Fig. 6. In either,
the light passing through the
film falls directly on a photo-
electric cell or is transmitted
to it through a suitable com-
bination of lenses and prisms.
Usually the photocell optical
system subtends a solid angle
of less than 2-rr radians as
measured from a point on the
sound track. Light passing
through the film emulsion is
scattered through a variable
solid angle depending on the
density (Callier effect), so
that at the higher densities a smaller proportion of the transmitted light reaches the
photocell. This gives the effect of increased density gradation (gamma) and must be
taken into account in processing variable-density sound tracks.
Pushpull sound tracks require two photocells and suitable means for reversing the phase
of one track with respect to the other. A typical pushpull reproducer, simplified, is shown
in Fig. 7.
Double Cathode
Photocell^ Push PuH
Flint J Transformer'
Condenser
FIG. 7.
Objective Lens
Separation
Optics
Push-pull Reproducer Optical System
In the reproduction of photographic sound tracks there are unavoidable losses in output
related to the speed with which the sound track is moved, and the dimensions and relative
positions of recording and reproducing slits. Both the recording and the reproducing
light beams should be exactly perpendicular to the direction of the film motion. Any
deviation from this direction is called an error in azimuth and introduces a loss at high
frequencies. Another important loss is due to the impossibility of producing on the sound
track a line of light which is infinitely narrow. These conditions produce loss of efficiency
SOUND-ON-FILM REPRODUCING SYSTEMS
13-53
at higher frequencies and in variable-area tracks may also introduce distortion. Figure S
shows typical loss curves of these effects plotted from the following equations.
VARIABLE-DENSITY SOUND TRACKS. Effect of image width for zero azimuth:
Scanning loss in decibels - 20 logio
CD
where / = frequency in cycles per second, 0 = half imag? width, and V = film velocity.
Effect of azimuth for fixed image width:
Scanning loss in decibels =
2r/j3 sec a
2yfl tan a
V
(2)
where I = half width of sound track, and a. — azimuth deviation angle.
If the azimuth is zero the last equation reduces to the equation preceding it. For very
small angles (0° to 6°),
which covers the cases
of practical interest,
£ sec a. — I tan a. Hence
in the azimuth-loss equa-
tion the image-width fac-
tor becomes equal to the
azimuth factor when the
azimuth deviation is equal
to the effective slit image
width; i.e., the scanning
loss for a particular azi-
muth deviation is equal to
that of an image width of
the same distance along
the length of the film.
25
1000
2 345
Frequency in Cycles per Second
789 10,000
FIG. 8. Loss Dae to Finite Sfit Width
VARIABLE-AREA SOUND TRACKS. For variable-area sound tracks the calcula-
tion of the effect of the aperture on fundamental response and generation of harmonics
becomes considerably more complicated and involves a number of assumptions that are
not always realized in practice. However, the general effects may be obtained by assuming
an ideal record in which the exposed portion has uniform density such as would be realized
with an infinitely narrow recording slit and an ideal film emulsion. The effect of finite
reproducing-slit width (with no azimuth error) is a reduction in response at high fre-
quencies exactly the same as shown above for variable-density sound tracks. On the
other hand, when the same ideal variable-area record is reproduced by means of a finite
slit not perpendicular to the direction of motion, the loss in fundamental amplitude for a
bilateral track is given by '
- — I
2am €
and the ratio of second harmonic to fundamental by
(4)
where 2e = width of reproducing image, a — width of unmodulated unbiased track, and
m = per cent modulation, and
. (=)•«£)
(46)
and p = cotangent of angle of azimuth deviation; also Ji and J2 are Bessel functions of
the first and second order respectively.
Third and higher harmonics are also produced by an azimuth deviation of the reproduc-
ing slit. Distortion may also be caused by the finite width of the recording slit, but it
may be compensated to some extent by choosing a suitable density for the print. The
13-54 ELECTROMECHANICAL-ACOUSTIC DEVICES
2.4
/
^
^
a
0
8
/
/
g 1.6
V
/
/
to
/
/\
to,
/
/
"\
Tz
n a —
ST
Q °-4
0
^~~*
<^S
!
\
) 0.
4 0
8 1.
2 1
6 2,
0 2.
4 2
8 3.
2 3.
6 4.
photographic image spread in the positive, then, to a first approximation, compensates
for both the finite recording slit width and the negative image spread.
Distortion may also occur in the reproduction of variable-area sound records as the
result of uneven illumination along the length of the reproducing slit. Although the
amount of such distortion depends on the type of variable-area track and on the type
and amount of unevenness of illumination, proper design of the reproducer optical system
and a reasonable degree of adjustment should result in harmonics not more than 3 per
cent of the fundamental (for full modulation) and in most cases considerably less.
In addition, variable-area records will obviously be distorted if the center line of the
record in the reproducer is displaced from the center line of the slit image so that part of
the record is not scanned. It is for this reason that 0.076 in. is considered the maximum
track width for distortionless reproduction since with a standard 0.084-in. scanning image
a tolerance of ±0.004 in. is then allowed for film weave.
PHOTOGRAPHIC REQUIREMENTS. The principal photographic requirement of
sound recording is that the variation of light from the average amount transmitted by the
film in the reproducer must
be proportional to the cor-
responding variation from
the average amount of light
transmitted by the record-
ing modulator. This gen-
eral relation is true for
both variable-density and
variable-area tracks.
For a variable-density
track, the exposure varies
from point to point along
the length of the track.
Figure 9 shows the manner
in which exposure and den-
sity are related in a typical
film emulsion. The exact
shape, and particularly the
slope of the central portion
of the H and D curve, depend on the development as well as the photographic properties
of the film, but most H and D curves have a portion that is essentially straight when
plotted as shown. The slope of the straight portion is called gamma, -y. If, when a nega-
tive is printed, a similar curve is drawn relating the exposure of the negative to the density
of the positive, the slope of the straight portion of this curve is the overall gamma. It can
be shown that for minimum distortion in variable-density recording the overall gamma
should be unity. In this computation factors such as the Callier effect (projection factor)
and the departure of actual gammas from the values measured by a sensitometer must
be taken into account. Since the positive film carries both sound and picture, both images
must be given the same development. The positive gamma is chosen to be suitable for
the picture and is usually about 2.2. Consequently, the negative of a variable-density
sound track is developed to a gamma of about 0.4 when measured on type 2B sensitometer.
Although optimum values of gamma and density for variable-density records can be
obtained with a fair degree of accuracy from sensitometric measurements, the simplest
and most reliable determination of these constants is made by means of intermodulation
tests. Such tests measure the non-linear distortion in a print made from a negative on
which two frequencies (usually 60 and 1000 cycles) are simultaneously recorded. Not
only is this form of test more sensitive than a measurement of harmonics of a single
frequency but also it corresponds more closely to audible distortion in commercial
records.
In processing variable-area records the aim is to obtain minimum density in the clear
area and maximum density in the exposed area. These are obtained by developing both
negative and positive to relatively high gammas, although excessive development may
result in fog in the clear area.
Variable-width records are also subject to non-linear distortion if they are not given
proper exposure and development. This distortion is frequently due to spreading of the
image and produces an effect similar to rectification. Optimum processing is determined
by "cross-modulation" tests in which a modulated high frequency is recorded. Distortion
is measured by the amount of low frequency produced by the photographic rectification
of the modulated high frequency. Distortion may also be caused by non-linearity of the
modulator and may be measured by harmonic or intermodulation tests.
Log Exposure
FIG. 9. H and D Curve
DEFINITION OF EFFECTS 13-55
BIBLIOGRAPHY
All references are to the Journal of the Society of Motion Picture Engineers unless otherwise noted.
General References
Academy; of Motion Picture Arts and Sciences, Motion Picture Sound Engineering. Van Noetraad.
New York (1938). ^^
Academy of Motion Picture Arts and Sciences, Recording Sound for Motion Pictures. McGraw-Hill,
New York and London (1931).
Talbot, R. EL, Some Relationships between the Physical Properties and the Behavior of Motion
Picture Film, Vol. XLV, 3, p. 209 (September 1945).
Kellogg, E. W., The ABC of Photographic Sound Recording, Vol. XLIV, 3, p. 151 (March 1945).
Iroye, D. P., and K. F. Morgan, Sound Picture Recording and Reproducing Characteristics, Vol. XXXII,
6, p. 631 (June 1939), and Vol. XXXIII, 1, p. 107 (July 1939).
Honan, E. M., and C. R. Keith, Recent Developments in Sound Tracks, Vol. XLI, 2, p, 127 (August
Light-valve Method
MacKenzie, D., Sound Recording with the Light Valve, Trans. Soc. Mat. Pict. Engrs., VoL XII, 35,
p. 730 (September 1938).
Shea, T. E., W, Herriott, and W. R. Goehner, The Principles of the Light Valve, VoL XVIII, 6, p. 697
(June 1932).
Frayne, J. G., and H. C. Silent, Push-pull Recording with the Light Valve, VoL XXXI, 1, p. 46
(July 1938).
Refiecting-galvanometer Method
Dimmick, G. LM Galvanometers for Variable Area Recording, Vol. XV, 4, p. 428 (October 1930).
Batsel, M. C., and E. W. Kellogg, The RCA Sound Recording System, VoL XXVIII, 5f p. 507 (May
1937).
Dimmick, G. L., The RCA Recording System and Its Adaptation to Various Types of Sound Track,
VoL XXXIX, 3, p. 258 (September 1937).
Kerr Cell Method
Zworykin, V., L. B. Lynn, and C. R. Hanna, Kerr Cell Method of Sound Recording, Tram. Soc. Moi.
Pict. Eng., VoL XII, 35, p. 748 (September 1928).
Ground-noise Reduction
KreuzerT B., Noise Reduction with Variable Area Recording, Vol. XVI, 6, p. 671 (June 1031).
Silent, H. C., and J. G. Frayne, Western Electric Noiseless Recording, VoL XVIII, 5, p. 551 {May 1932).
Kellogg, E. W., Ground Noise Reduction System, VoL XXXVI, 2, p. 137 (February 1941).
Scoville, R. R., and W. L. Bell, Design and Use of Noise Reduction Systems, Vol. XXXVIII, 2, p.
125 (February 1942).
Reproducing Systems
Cook, E. D., The Aperture Effect, VoL XIV, 6, p. 650 (June 1930).
Stryker, N. R., Scanning Losses in Reproduction, VoL XV, 6, p. 610 (November 1930).
Cook, E. D., The Aperture Alignment Effect, VoL XXI, 5, p. 390 (November 1933).
Foster, DM Effect of Orientation of the Scanning Image on the Quality of Sound Reproduced from
Variable Width Records, VoL XXXIII, 5, p. 502 (November 1939).
Batsel, M. C., and C. H. Cartwright, Effect of Uneven Slit Dlumination on Distortion in Several Types
of Variable Width Records, VoL XXIX, 5, p. 476 (November 1937).
Carlson, F. E.t Properties of Lamps and Optical Systems for Sound Reproduction, VoL XXXIII,
1, p. 80 (July 1939).
Photographic Tone Reprodttctwrn
Hardy, A. C., The Rendering of Tone Values in the Photographic Recording of Sound, Tram. Soc.
Mot. Pict. Eng., VoL XI, 31, p. 475 (September 1927).
Jones. L. A., On the Theory of Tone Reproduction, with a Graphic Method for the Solution of Prob-
lems, Vol. XVI, 5, p. 568 (May 1931).
Mees, C. E. K., Some Photographic Aspects of Sound Recording, VoL XXIV, 4, p. 285 (April 1935).
Measurement of Distortion
Baker, J. O.T and D. H. Robinson, Modulated High Frequency Recording as a Means of Determining
Conditions for Optimal Processing, VoL XXX, 1, p. 3 (January 1938).
Frayne, J. G., R. R. Scoville, Analysis and Measurement of Distortion in Variable Density Recording,
VoL XXXII, 6, p. 648 (June 1939).
Dimensional and Other Standards
Motion Picture Standards (Z22) are obtainable from the American Standards Association, 70 E. 45 St.,
New York, N. Y., or from the Society of Motion Picture Engineers, 342 Madisoa Aw., New York,
N.Y.
PIEZOELECTRIC CRYSTALS
By W. P. Mason
31. DEFINITION OF EFFECTS
A piezoelectric crystal is a crystal which suffers a change in dimension or form propor-
tional to an applied electrical potential, for small applied potentials, and conversely gen-
erates a surface charge when subject to stresses. These properties of piezoelectric crystals
allow a coupling to be made between an electrical circuit driving a mechanical circuit or
13-56 ELECTROMECHANICAL-ACOUSTIC DEVICES
with the mechanical properties of the crystals themselves used to create an electric voltage
as a result of mechanical motion. When a crystal is used to couple an electrical to a
mechanical system it is said to be an electromechanical transducer. An example of such a
device is a crystal used as the pickup unit in a phonograph, in which function it transforms
the 'mechanical vibrations of the record into electrical vibrations which are amplified and
produce sound vibrations through the loudspeaker. When the mechanical resonances of
the crystal itself are used, the crystal is said to be a piezoelectric resonator or a piezoelectric
oscillator.
The piezoelectric effect was discovered in 1880 by the brothers Jacques and Pierre Curie.
They discovered first the "direct" effect, which is the production of charge on a crystal
surface due to the effect of a mechanical force applied to the crystal surface. They also
measured the "inverse" effect, which is the change in shape of the crystal due to an applied
potential. Voigt (Lehrbuch der Kristallphysik, B. Teubner, 1910) later showed that all
the linear properties of a crystal under applied stresses, potentials, and temperatures re-
sulted in strains, electrical displacements, and increases in heat energy according to the
equations
63
Si - S SijTf -f S dthEk + on BB (i, j = 1, • • -, 6)
.7=1 Jfc-1
— = 23 difTi + S r- Etc -f PI 50 (fc, I = 1, • • •, 3) (1)
47r J~i A=l47r
6 3
8Q = £ 9*/2V + 2 SpkE* + PCP 60
where Si(i — 1 to 6) are the six strains that can exist in a solid body, T3-(j = 1 to 6) are
the six stresses in the body, JSk(k = 1 to 3) the three potential gradients (ratio of total
potential divided by distance over which they are applied) that exist along the three axes,
9 is the absolute temperature in degrees Kelvin and 59 the increase in temperature,
Di(l = 1 to 3) is the electric displacements along the three axes, and 8Q is the increment
in heat energy due to applied stresses, fields, and temperature increments. (These symbols
have now been standardized by the Institute of Radio Engineers.)
The first equation says that any one of the strains, for example Si, is in general propor-
tional to the six stresses, the three electric fields along the three axes, and the temperature
increment 56. The constants $»•/ which relate the strains to the applied stresses are the
elastic moduli of compliance. Since it can be shown that SH — Sji there are 21 such con-
stants for the most general crystal, a triclinic crystal. If any elements of symmetry exist
in the crystal the number of independent constants is reduced. For example, ammonium
dihydrogen phosphate (ADP) has six independent elastic compliances, quartz has seven,
and Rochelle salt (sodium potassium tartrate) has nine. The diu constants are the piezo-
electric constants which relate the strains to the applied fields. For the most general
crystal there are 18 independent constants, but for more symmetrical crystals the number
is reduced. ADP has two independent constants, quartz two, and Rochelle salt three.
The ai constants are the six temperature expansion coefficients which relate the six strains
to the applied temperature increase 56.
The second equation states that the electric displacement is proportional to the applied
stresses (the constants of proportionality being again the piezoelectric constants), to the
applied fields (the constants of proportionality being the dielectric constants e&z) , and to
the increase in temperature 56 (the constant of proportionality being the pyroelectric
constants pi) . (The equation as written is valid for the cgs system of units. For the mks
system the 4-rr is removed from Di and ejt.) Since l/(47r) times the normal component of
the electric displacement at the surface of the crystal is equal to the surface charge <r, this
equation shows the origin of the direct piezoelectric effect (while eq. [1] expresses the in-
verse effect).
The third equation states that the increment of heat 8Q is proportional to the stresses,
the fields, and the applied temperature increment. The first effect is called the stress-
caloric effect, and the constant of proportionality is the absolute temperature 6 times the
temperature expansion coefficients a,. The second effect is called the electro caloric effect,
and the constant of proportionality is the absolute temperature 6 times the pyroelectric
constant pk. This last is the ratio of the electric displacement to the applied temperature
56 measured at constant stress and constant field. The last term in the third equation
expresses the increase in heat energy due to a temperature increase 59, and the constant
of proportionality is the density p times the specific heat at constant stress Cp. In all
these equations the constants of proportionality for one variable are measured with the
DEFINITION OF EFFECTS 13-57
other two variables in the equation held constant. Thus s,-;, for example, could be written
with two superscripts «f/s.e, indicating that in determining the constants the fields E
and the temperature 6 are held constant. They are therefore the constant field, isothermal
elastic compliances. Similar superscripts can be written for the other terms.
For most piezoelectric applications the vibrations are so rapid that there is no time for an
interchange of ^ heat, and adiabatic conditions prevail. This can be taken account of in
eq. (1) by setting 5Q = 0. If we do this and eliminate £6 from the remaining equations
we have two equations given by
6 3
st = 2 *a*Ti + 2 **#*
j-i *=i
n 6 3 - (2)
All these constants are adiabatic, and they are related to the isothermal constants of eq. (1)
by the relations
where the constants on the left side are understood to be adiabatic. Equations (2) repre-
sent all the linear adiabatic relations existing for a piezoelectric crystal, while eqs. (1) give
all the isothermal linear relations existing for a piezoelectric crystal. Two second-order
effects, the piezo-optical, and the electro-optical, are also of some interest, but they will
not be discussed here. They result from a change in the dielectric constant as a function
of applied stresses and applied fields respectively.
For ferroelectric crystals such as Rochelle salt the constants in the equations of the
form (2) go through very wide variations over a temperature range. It has been found *
that, if the electric displacement is used as the dependent variable instead of the field,
the resulting constants are nearly independent of temperature. These relations can be
obtained from eqs. (2) by solving in terms of DI and TJ; they are
6 3
£* = - 2 &>Tj -f £ $klTDl (4)
.7=1 1=1
where
r — l)k+i\k,i
fit? = - - '— - ; gu = fadu + ferf23 + &k*d*i
-f rf*4|j4 + diagfr -f
and A is the determinant
en €12
A =
and Afc'z is the determinant obtained by suppressing the &th row and Zth column.
A ferroelectric crystal is one which shows a spontaneous polarization over a given
temperature range. This is due to the movable electric dipoles exerting a mutual reaction
and lining up for one direction of the crystal. The effect is similar to the ferromagnetic
effect in magnetic substances and is accompanied by similar effects. The polarization vs.
potential curves show hysteresis effects and very high dielectric constants. Large piezo-
electric effects exist in the ferroelectric range, and Rochelle salt, for example, has a du
piezoelectric constant which may be 1000 times as large as that for a quartz crystal. The
limiting temperatures for the ferroelectric regions are called the Curie temperatures.
For Rochelle salt these are —18 and +24 deg cent. Other ferroelectric crystals are also
known, notably potassium dihydrogen phosphate and potassium dihydrogen arsenate (see
Busch, "Neue Seignette Elektrica," Helv. Phys. Ada, II No. 3 [1938]), but their Curie
temperatures are very low, namely, — 151 and — 182 deg cent. RocheUe salt was the
first crystal discovered that had its ferroelectric region in the room-temperature range.
This fact accounts for its wide use in acoustic devices in spite of its poor mechanical and
* See W. P. Mason, A Dynamic Measurement of the Elastic, Electric, and Piesoelectric Constants
of RocheUe Salt, Phys. Rev,, Vol. 55, 775 (1939), and H. Mueller, Properties of Rochelk Salt, Pk&s.
Rev., 57, 829 (1940).
13-58 ELECTROMECHANICAL-ACOUSTIC DEVICES
chemical properties. Another ferroelectric crystal, barium titanate, has recently been
discovered which has a large electrostrictive effect. This crystal in ceramic form may
be an important electromechanical transducing element (Mason, "Electrostrictive Effect
in Barium Titanate Ceramics," Phys. Rev., Vol. 74, No. 9, pp. 1134-1148, Nov. 1, 1948).
32. APPLICATION OF PIEZOELECTRIC CRYSTALS
The piezoelectric effect remained a scientific curiosity from the time of its discovery
until the time of World War I, 1914-1918. During that time Professor Langevin in Paris
devised an underwater sound-locating device using quartz crystals to convert alternating
electrical energy into sound vibrations in water. The sound beam was sent out into the
water and was reflected back from an object or the bottom of the ocean. This reflection
impinged on the crystal transducer and generated an electrical voltage which could be
detected by vacuum-tube devices. This use was a forerunner of the fathometers and
•underwater sound-locating devices that have been widely used by the Navy. Although
quartz was originally used for this purpose it has been displaced by Rochelle salt and
particularly a new crystal developed during World War II, the ammonium dihydrogen
phosphate or ADP crystal. This crystal has so many mechanical, chemical, power-
handling capacity, and temperature advantages over Rochelle salt that it appears likely
to replace all other transducing elements for underwater sound applications.
In 1922 it was shown by Professor Cady of Wesleyan University that very stable
oscillators could be obtained by using quartz crystals as the frequency-controlling element.
These have been applied to controlling the frequency of broadcasting stations and radio
transmitters in general. Quartz crystals using some one of the low-temperature-coefficient
crystals described in article 33 produce the most stable oscillators and the best time-
keeping systems that can be obtained. The use of crystals to stabilize oscillators was so
prevalent during World War II that over 30,000,000 crystals were produced in a single
year for this purpose.
Another application of piezoelectric crystals is in producing very selective filters. On
account of the very high Q existing in crystals they can practically eliminate the effect
of dissipation in filter structures. Such filters have been widely applied in the long-dis-
tance telephone lines and in single-sideband transatlantic radio telephone systems.
Narrow-band crystal filters have been used in picking off single frequencies and narrow
bands of frequencies for control and analyzing purposes. For this application quartz
crystals have been mostly used. However, it appears that the requirements are lenient
enough to allow some of the synthetic crystals to be employed.
Besides producing and detecting sound in liquids, crystals have been used to produce
and detect vibrations in gases and solids. On account of their high mechanical and
electrical impedances crystals are at somewhat of a disadvantage in coupling to low-
mechanical-impedance air waves. By using bimorph types of units which employ bending
or flexnral vibrations the mechanical impedances of crystals can be lowered. For sound
pickup devices the high electrical impedance is not a disadvantage, for they can be worked
directly into the grid of a vacuum tube which inherently is a high impedance. Hence
large numbers of crystals have found uses in microphones. For this purpose Rochelle salt
is common, but the constants of ADP are favorable enough so that they may displace it.
Crystals have also been used in receivers, relays, oscillographs, and other devices for
which displacements are required for a given applied voltage. For this purpose, crystals
having large d piezoelectric constants are required, and Rochelle salt is universally used.
On account of the large variation of d with temperature such devices are not very stable
and reproducible and hence are unsuitable for high-quality equipment.
Crystals have also been employed in producing very high-frequency vibrations in gases,
liquids, and solids. For this purpose quartz is the almost universal choice since it can be
ground very thin and can be used to produce high frequencies. X-cut quartz is utilized
to set up longitudinal vibrations and Y-cut quartz to produce shear vibrations. Such
high-frequency sound waves are applicable for testing steel castings and other solid
materials for flaws (Firestone, The Supersonic Reflectoscope, .7". A.S.A., Vol. 17, No. 3
[January 1946]). They have also been utilized to study the properties of liquids, gases,
and solids and the way in which they vary with frequency.
33. PROPERTIES OF QUARTZ
There are at least 500 crystalline substances that have been tested and found to be
piezoelectric, and it is to be presumed that among the many thousands of compounds that
will form into crystals in the 20 out of the 32 crystallographic classes that may be piezo-
PROPERTIES OF QUARTZ
13-59
electric most of them will show some piezoelectric activity. However, only three crystals
nave received wide application in practical devices: quartz. Rochelle salt, and ammonium
dihydrpgen phosphate (ADP). A fourth crystal, tourmaline, has received a limited appli-
cation in sound-measuring devices because it is sensitive to hydrostatic pressures. It is to be
expected, however, that, with several large laboratories actively engaged in investigating
new piezoelectric materials, many more crystals will eventually find practical appHcation.
It is the purpose of the following sections to discuss the properties and useful cuts of
quartz, Rochelle salt, and ADP.
PHYSICAL PROPERTIES OF QUARTZ. Quartz is described by the chemist as
silicon dioxide, Si02, and it crystallizes in the trigonal trapezohedral class. The Z or optic
axis is an axis of threefold symmetry; i.e., if one measures any property of the crystal at a
definite position in the crystal, this property will be repeated at angles of ±120° rotation
about the^Z axis. The melting point of quartz is 1750 deg cent, the density 2.65, and the
hardness is 7 on Mohs' scale. Under atmospheric pressure, a or low-temperature quartz
transforms into ft or high-temperature quartz at 573 deg cent. Under stress this trans-
formation temperature is lowered. Alpha quartz is insoluble in ordinary acids but is
decomposed in hydrofluoric acid and in hot alkalies. Quartz is soluble to some extent in
water at high pressures and temperatures. In an enclosed system, crystalline quartz will
dissolve in water to the extent of
3 grams per liter at 350 deg cent.
Powdered fused quartz, which has
a larger surface-to-volume ratio,
will dissolve to a considerably
larger extent.
Quartz is found principally in
Brazil in several different types of
deposits (see Stoiber, Tolman, and
Butler, Geology of Quartz Crystal
Deposits, Am. Mineralogist, Vol.
30, 245-268 [1945]). The prepon-
derance of the crystals found is in
the lower-weight class as shown by
the table. Most of the clear quartz
has recognizable natural faces, but
some, particularly river quartz,
has no natural faces.
Quartz occurs in optical right-hand and left-hand forms; i.e., the crystal will rotate the
plane of polarization of polarized light passing along the Z or optic axis counterclockwise
(left handed) or clockwise (right handed) from the point of view of the observer facing the
source of light. Most crystals have sections with both handedness. In general, the middle
section is likely to be all of one hand while the outside sections may have parts of each
handedness. A conoscope may be used to locate the optic axis and will also show the
handedness and position of any optical twinning. The principle of the conoscope is shown
by Fig. 1. Light from the source is sent through a polarizer aad through the converging
lens LI. This lens sends converging or conical beams through the crystal which are
gathered by the second lens, focused, and sent through the analyzer. In practice the
lenses and crystal are immersed in a liquid having the same index of refraction as the crystal
along its optic axis. Such liquids
may be mixtures of Decaliii and
Dowtherm or dimethyl phthalaie
and a monochlor naphthalene.
The crystal breaks up all rays not
parallel to the optic axes into two
components which travel with dif-
ferent velocities. Hence the an&-
FIG. 1. Principle of Conoscope lyser » not able to extinguish the
light that has traversed the crystal
except at angles for which the two rays are in opposite phase. Hence one sees a series of
rings in the conoscope when the direction of the Z axis is along the line between the
source and the eye. Owing to the rotation of the plane of polarization in the crystal one
finds that the rings either expand or contract for a right- or left-handed crystal respectively
for a clockwise rotation of the analyzer. This gives a method of determining the handed-
ness of the crystal. Optical twinning also shows up in a viewing system of this type, for
it deforms the ring pattern. If plane rays rather than conical rays are used, and a source
of white light, color effects also show up the position of the optical twinning.
Crystal Weight Groups
weight in grams
Percentage of the Total Number
of Crystals Which Were In Each
Weight Group
200- 300
3Q&- 50Q
500- 700
55.5
29.5
I©. 4
700- !,000
1,000- 2,000
2,000- 3,000
2.1
1. 8
0.5
3rOOO- 4,006
4,000- 5,000
5,000- 7,000
0.2
<0.1
<0.1
7,000-10,000
<Q,f
13-60 ELECTROMECHANICAL-ACOUSTIC DEVICES
NORMAL ALPHA QUARTZ
The Dauphine or electrical type of twinning also exists in quartz. It results from a 180°
change in the direction of the crystal atomic arrangements. As shown by Fig. 2, the silicon
atoms normal to the Z axis are arranged in near hexagons all pointing in one direction.
If the temperature is raised above 573 deg cent a change in the arrangement to the hexag-
onal pattern shown in the middle occurs. The result is high-temperature or /3 quartz.
As the temperature is decreased below 573 deg, the crystal may return to the form at
the bottom, or part of it may return to this form and part to the form in which the near
hexagons point in the opposite direction. If both forms exist the crystal is said to have
electrical twinning. The best method of detecting elec-
trical twinning is by etching the surface with hydrofluoric
acid, which eats away the crystal at rates depending on
the orientation of the crystal surface. Since the two
twinned areas will develop etch pits that point in op-
posite directions, grazing light will cause one part to re-
flect brightly while the other reflects diffusely, and hence
one can see the parts that have different regions of elec-
trical twinning. Since the piezoelectric effect is opposite
for the two twinned areas, it is necessary that there be
only one region in a useful crystal. Electrical twinning
usually occurs in an untwinned plate if it is taken above
the inversion point. It may also occur at lower temper-
atures if stress is applied. Such twinning has been ob-
served when a hot soldering iron is pressed against a
crystal, or it may even occur when the crystal is sawed.
Wooster (Nature, Vol. 157, No. 3987 [March 30, 1946])
has found that the electrical twinning can be removed by
exerting a twist around the Z or Z' axis and heating the
crystal nearly to the inversion point.
Other defects in quartz crystals are (1) "bubbles":
bubble-like cavities which may be fine or large; (2) veils,
heavy or fine, which are more or less continuous sheets
of small bubble-like cavities; (3) clouds or haze: aggre-
gates of fine bubble-like cavities; (4) ghosts or phantoms:
outlines of earlier growths within the crystal, usually
marking what were once edges of adjoining faces which
xxxx
BETA OR HIGH -TEMPERATURE
QUARTZ
TWINNED ALPHA QUARTZ
PIG. 2. Arrangement of Silicon
Atoms in Quartz Normal to Z Axis
become visible when a beam of light is reflected from the minute fractures or parting
planes that outline them; (5) fractures. All these defects can be observed by shining a
strong light through the crystal at right angles to the direction of observation. The
crystal is usually immersed in an inspection tank which is filled with a liquid having the
same index of refraction as the crystal. Opinions differ on how many inclusions or
bubbles of a small size can be tolerated in the finished crystal.
All the inspection and orienting instruments as well as the methods of sawing and pre-
paring the crystals are completely described in R. A. Heising, Quartz Crystals for Electrical
Circuits, Van Nostrand, 1946, and in the May- June 1945 issue of the American Mineralogist.
USEFUL CRYSTAL ORIENTATIONS. The modes of motion and the properties of
these modes depend markedly on how crystal plates are oriented with respect to the
natural crystal faces. Figure 3 shows a natural quartz crystal, the three crystallographic
axes, and some of the more important special cuts that have found use in the radio and
telephone art. The Z or optic axis of the crystal is along the long direction of the crystal;
the X axis lies through one of the apexes of the hexagon; and the T axis is normal to the
other two in a right-handed system. The piezoelectric, elastic, and dielectric equations
of quartz take the form
Si = 811*3*1
duEx
-f
84 =
Ss =
(5)
47T
<?z = — —
PROPERTIES OF QUAJRTZ
13-61
ZERO
TEMPERATURE-COEFFICIENT
OSCILLATORS AND FILTERS
LOW-FREQ1
HIGH-FREQ:
AT (+35°'15')
BT (-49°)
DT (-52°!
ET (+&6°)
* FT (-57°)
\
S&--TV
ZERO COUPLING (Sa4=0)
-13* FILTERS
-3-5-7 HAF*4ONltCS
0° OSCILLATORS \
FUNDAMENTAL AND *
SECOND HARMONIC
MT LONCTTUOtMAl.
CRYSTAL
NT FLEXURE CRYSTAL
LOW Te-*PERATUR£- COEFFICIENT
OSCILLATORS * * +5° FILTERS
AND FILTERS DOUGHNUT .
ZERO TEMPERATURE-COCFFICIENT
FIG. 3. Principal Cuts of Quartz
where £1, &, S* are the three elongation strains along the X, F, and Z axes respectively;
S4, S6, and S6j the three shearing strains; jfi, T2, T3, the three tensional stresses; T*, T^
and TS, the three shearing stresses; Ex, Eyj ESl the three fields; Dx, Dyj Z>2, the three elec-
trical displacements which at the outer surfaces are equal to the surface charge 4iro-a.,
47ro-y, and 47rcrz. In cgs units the elastic, piezoelectric, and dielectric constants have the
values (see Mason, "Quartz Crystal Applications," B.S.TJT., VoL 7TX7T, No. 2 {July
1943]) :
«ii* = 127.9 X 10~14 X cmVdyne
SnE = -15.35
' = -11.0
1 = -44.6
; - 95.6
' = 197.8
= 2(snE - sis*) = 286.5 X 10 ~14
« —6.76 X 10~8 statcoulomb/dyne
= 2.56 X 10~8
(6)
4.5S :
4.70
statcoulomb
statvolt
for the nxks system the elastic compliances are multiplied by 10, the piezoelectric constants
divided by 30,000, and the dielectric constants multiplied by the factor S.S5 X 10"12.
13-62 ELECTROMECHANICAL-ACOUSTIC DEVICES
X-CTJT CRYSTALS. These equations are useful in predicting the type of motion
that will be generated in a given type of cut and the magnitude of the electromechanical
coupling. For example, the first equation of eq. (5) shows that a strain Si, which is an
elongation along the X axis, will be generated by a field applied along the X axis. The
applied field will then generate a thickness longitudinal mode since the motion is in the
same direction as the applied field. If the thickness is made small this type of crystal can
produce a very high frequency, and it was originally used to control oscillators. Because
of their poor temperature coefficient, such crystals have largely been replaced in the
control of oscillators by AT and BT thickness shear mode crystals which have much
better properties. X-cut crystals, however, will produce ultrasonic vibrations in solids,
liquids, and gases, and such waves have been used in studying the properties of these
materials and also in flaw detectors (see Firestone, /. A.S.A. [January 1946]} which deter-
mine whether any cracks or irregularities occur in metal castings. For this purpose it is
desirable to transform as much input electrical energy as possible into mechanical energy.
A measure of the efficiency of this conversion for statically or slowly varying applied fields
is the electromechanical coupling factor k, which is defined by the equation
fc = <W^T- = °'095 (7)
* Ei
where CHE is the effective elastic constant for a thickness mode. This is equal to
CUE = 8.60 X 10U dynes per cm2 (8)
Inserting the values given in eq. (7), we find that the coupling is about 9.5 per cent. This
means that, for a static field, the square of k or about 1 per cent of the input energy is
stored in mechanical form. For alternating fields near the resonance of the crystal a
considerably larger part, in fact, nearly all, can be converted into mechanical energy if
the shunt capacity is tuned by a coil, but, nevertheless, the coupling is a measure of the
width of the frequency range for which this conversion can be done efficiently. If /g is
the highest frequency and /A the lowest frequency for which the loss is not more than 50
per cent it can be shown that
/~ /i _i_ z>
(9)
Some synthetic crystals such as lithium sulfate and L-cut Rochelle salt have coupling
factors of 0.35 to 0.4 and are to be preferred when it is desired to radiate a wide band of
frequencies, but for high frequencies X-cut quartz is commonly used on account of its
excellent mechanical properties.
The second equation of (5) shows that a strain $2, which is an elongation along the Y
axis, is excited when a field is applied along the X axis. Since the long direction of the
crystal is taken along this direction this mode of motion is called a length longitudinal
mode. It has been used to some extent to drive low-frequency oscillations in gases, liquids,
and solids. Two modifications of this cut have received considerable use in the construc-
tion of quartz crystal filters. These cuts are the — 18° -ST-cut crystal and the +5° X-cut
crystal shown by Fig. 3. The -—18° cut is used because it produces a very pure frequency
spectrum giving only a single resonance over a frequency range of 3 to 1 (see W. P. Mason,
Electrical Wave Filters Employing Quartz Crystals as Elements, B.S.T.J., Vol. XIII
[July 1934]}. The +5° .XT-cut crystal is
used because it is the best orientation of
the X cuts for giving a low temperature
coefficient of frequency. By putting a
divided plating on the crystal as shown by
Fig. 4 this crystal can be driven in a flexure
mode at much lower frequencies than can be
realized with a longitudinal mode. It has
FIG. 4. Plating Arrangement for Driving a keen usec* *or picking off single-frequency
Longitudinal Crystal in Flexure pilot channels for controlling the gain of a
carrier system.
The temperature coefficient of the +5° X-cut used for both longitudinal and flexure
modes can be improved by rotating the thickness around the length of the crystal. This
results in the M T and NT crystals shown by Fig. 3. These have temperature coefficients
under one part in a million per degree centigrade but a smaller coupling than the equivalent
-1-5° X-cut crystals. (See Mason and Sykes, Low Frequency Quartz Crystal Cuts Having
Low Temperature Coefficients, Proc. LR.E., Vol. 32, No. 4 [April 1944].)
F-CUT CRYSTALS. When a field Ev is applied along the Y axis, eq. (5) shows that
two types of strain are generated, S& and SQ. Both these strains are shearing strains which
PEOPERTIBS OF QUARTZ
13-63
distort a square in the crystal into a rhombus as shown by Fig. 5. The Sg strain, shown
in Fig. 5, distorts the crystal in the XZ plane; the & strain distorts the crystal in the XY
plane. ^ Since the field is applied along the thickness,
which is the Y direction, the first strain 5* is called a
face shear strain and Ss a thickness shear strain. The
frequency of a face shear mode is controlled by the con-
tour dimensions and hence will be relatively low. The
frequency of the thickness shear mode is controlled by
the thickness dimension] which can be made very small
and hence will result in a high frequency.
The 7-cut crystal was first used in the control of high-
frequency oscillators but on account of its high temper-
ature coefficient has largely been displaced by the AT
and BT crystals which are modified F-cut crystals. The
7-cut crystal is still used to generate shear vibrations in i ^X
solids. For this purpose it has a higher coupling than the /! ^
X cut, since the coupling for the shear thickness mode is *• — "
0.142
FIG. 5. Method for Obtaining a
, „ rt Longitudinal Vibration from a Shear
(10) Crystal
FREQUENCY CONSTANT IN KILOCYCLt
MILLIMETERS (Fxd)
« s 8 B K 8
—^e.
/
--—
f*
BC
>>
Vk
/
s.
\
/
\
\
I/
N
I^Y-CUT
/
/
\
AC XT S
H<
-6O -60-40-20 0 20 4O 6O 8O
ROTATION ABOUT X AXIS iN DECREES (9)
FIG. 6. Frequency Constants for Rotated F-cut Quartz Crystals
Rotations of the thickness direction around the X axis have resulted in rotated Y cuts
that have very favorable properties. Investigations made by Lack, Willard and Fair,
, Koga, Bechmann, and
Straubel have shown
how the properties of the
thickness shear mode
varied with angle of cut.
As shown by Fig. 3 all
the orientations result-
ing in useful crystals
have their length along
the X axis and their
thickness makes an angle
& with the Y axis. Fig-
ure 6 shows the fre-
quency constant (kilo-
cycles for a crystal 1 Tnm
thick) as a function of
the angle of rotation.
At an angle of rotation
of -f 31° and -59° the
frequency is minimum and maximum respectively. At these two angles, the mechanical
coupling between the thickness shear mode, and the face shear mode and overtones, be-
comes zero and a crystal is obtained which is much freer from extraneous modes of motion
than is the Y cut. Fig-
ure 7 shows a plot of
temperature coefficient
against the orientation
angle, and at 35° 15' and
— 49° crystals are ob-
tained which have zero
temperature coefficients.
These cuts, known as the
AT and BT crystals re-
spectively, have been
very widely used to con-
trol high-frequency oscil-
lators. Frequencies as
high as 10 megacycles
are used for fundamental
control, and by means
of mechanical harmonics
frequencies as high as 197
megacycles have been
TEMPERATURE COEFFICIENT IN PARTS
, PER MILLION PER *C
§ 8 i o fc 8 §
0 EXPERIMENTAL
CHECK POINTS
^i
/
/
\
\
BT
/
/
\
.AC
V3!
BO
/
>
s,
/
/
V
\
S
L>*«>.
— •*
-80
-60 -40 -20 0 2O 4O 60 8O
ROTATION ABOUT X AXIS JN DEGREES (6)
FIG. 7. Temperature Coefficients for Rotated F-cut Quartz Crystals
13-64 ELECTROMECHANICAL-ACOUSTIC DEVICES
obtained. (See Mason and Fair, A New Direct Crystal Controlled Oscillator, Proc. I.R.E.,
Vol. 30, 464-472 [October 1942].)
Since the AT and BT are relatively near in angle to the AC and BC cuts they have a
good frequency spectrum. Strong couplings still exist to flexure modes of motion. By
measuring the modes of motion as a function of the length, width, and thickness, dimen-
sional ratios can be obtained for which only the main mode exists for a large frequency
range on either side of the main frequency. (See Sykes, Modes of Motion in Quartz
Crystals, B.S.T.J., Vol. XXIII, No. 1 [January 1944J.) By maintaining this ratio fixed
as the thickness is changed, a good crystal free from resonances over a wide temperature
range is obtained. Crystals produced by the process of grinding to a set of predetermined
dimensions are called predimensioned crystals and usually result in a higher-activity
crystal and one having a smooth temperature frequency curve over a wide temperature
range.
Another manufacturing process called the edge grinding process is sometimes employed.
This consists in controlling the thickness dimension only and in removing troublesome
couplings by grinding the edges of the crystal until the crystal has a high activity and is
free from frequency hops over a temperature range. This process may be quicker for
crystals that do not have to satisfy stringent activity and temperature requirements but
is not likely to produce as satisfactory crystals as the predimensioning process. Thickness
vibrating crystals may either be ground or etched to frequency. On account of an aging
which appears to be due to loosely bound and misoriented layers of quartz on the surface
caused by sawing and lapping processes, it has become customary to etch crystal surfaces
to frequency, since this process removes the loosely bound material and leaves a surface
that does not age appreciably. The aging appears to be caused by the attack of water
vapor on the strained surface which results in either loosening or removing the strained
material. The first process causes a lowering of the Q of the crystal (ratio of reactance to
resistance) and a consequent lowering of the activity of the oscillator controlled by the
crystal; the second process causes an increase in the frequency of the crystal. Aging can
be prevented by etching the crystal surface to a depth of several microns or by hermetically
sealing the crystal.
Two other methods of adjusting the frequency of crystals have been employed. One
(see Sykes, High Frequency Plated Quartz Crystal Units for Control of Communications
Equipment, Proc. I.R.E., Vol. 34, No. 2 [February 1946]) etches the crystal frequency
above the desired frequency by a predetermined number of kilocycles and then lowers
the frequency by plating; by an evaporation process an amount of metal necessary to
load the crystal down to its desired frequency is added to the crystal. By this method the
frequency can be very accurately controlled in the final mounting. The other method
utilizes the recently discovered fact that exposure to X-ray irradiation lowers the elastic
constant of BT and AT crystals and hence lowers their frequency of oscillation (see
Frondel, Effect of Radiation on the Elasticity of Quartz, Am. Mineralogist, Vol. 30 [May
1945]). The effect is produced by electrons being expelled from orbits around silicon
atoms in the quartz and causing a lower energy of binding between molecules and hence a
slightly lower elastic constant. This effect amounts to 0.1 per cent frequency change at
the most and varies by considerable factors from crystal to crystal, presumably owing to
the amount of their impurity content. Exposure to X-rays causes a darkening of the
crystal, and the amount of darkening appears to be correlated with the amount of fre-
quency change. On account of the variability of the effect, this process has not had a
wide use.
Two other rotated F-cut crystals that can be given zero temperature coefficients are
the CT and DT face shear cuts (see Willard and Hight, Proc. I.R.E., Vol. 25, 549-563
[1937]) . These are nearly at right angles to the AT and BT cuts and use the same shearing
moduli in the face shear mode that the AT and BT do in the thickness shear mode. The
CT cut at +38° orientation as shown by Fig. 3 has a frequency constant of 308 kc-cm for a
square crystal and has been used in frequency-modulated oscillators in the frequency range
from 300 to 1000 kc. The DT crystal is smaller for the same frequency and is used in the
frequency range from 200 to 500 kc. Both these crystals had wide application in frequency-
modulated oscillators for tank and artillery radio circuits during World War II.
The final rotated F-cut crystal that has been used considerably for controlling very
precise oscillators for time standards and in the Loran navigation system is the GT crystal
(see Mason, A New Quartz Crystal Plate, Designated the GTT Proc. I.R.E., Vol. 28, 20-
223 [May 1940]). This crystal is produced, as shown by Fig. 3, by rotating the plane
by 51° 7.5' from Y and by rotating the length 45° from the X axis. Whereas most other
zero-temperature-coefficient crystals have a parabolic variation of frequency with tem-
perafenare about the zero temperature coefficient as shown by Fig. 8, this parabolic variation
is absent for the GT and a very constant frequency is produced over a wide temperature
PROPERTIES OF ROCHELLB SALT
13-65
range. Hence a very moderate temperature control produces a very constant frequency.
A crystal mounted by means of several wires soldered to its surface (see Greenidge, Mount-
ing and Fabrication of Plated Quartz Crystal Units, B.S.T.J., Vol. 23, 234 [July 1944J)
20
z
o
a
£
50
/ /LONG BAR» LENGTH \
/^Y ALONG X AXIS: \
/ )L>1ST HARMONIC \
/ / ^~2ND HARMONIC V
V
/v
/A
t
\
\
\\
\
10 2O 30 40 5O 60 70 »O 9O 1OO
TEMPERATURE IN DECREES CENTIGRADE
G. 8. Temperature Frequency Characteristics for Low-coefficient Quartz Crystals
110
is very stable, is little affected by shocks, and ages very little over a long period of time.
It constitutes an oscillator that maintains its frequency to 1 part in 109 or better over long
periods of time and has made possible the precise timing necessary in the Loran system
and in very stable time standards (see
Spencer Jones, Endeavor, Vol. 4, No. 16
[October 1945]). X-CUT CRYSTAL
34. PROPERTIES OF
ROCHELLE SALT
Rochelle salt is sodium potassium tar-
trate with four molecules of water of
crystallization (NaKC^Oe • 4H2O) and
forms in the orthorhombic bisphenoidal
class. The usual form of the crystal is
indicated by Fig, 9 (a), which shows the
directions of the X t Y, and Z axes. Since
the crystal has water of crystallization it
has a vapor pressure. As shown by Fig. ^) 45o_CUT
10, lower line, if the humidity of the sur-
rounding atmosphere is below 35 per cent
at 25 deg cent, the water-vapor pressure
of the crystal is greater than the vapor
pressure of water in the surrounding at-
mosphere and the crystal will lose water
and dehydrate. This causes a white
powder of dehydrated material to form on
the outside of the crystal which will ruin
the operation of the crystal if it becomes
too large. The crystal is stable between
35 and 85 per cent relative humidity (d) TORSIONAL X_M (e) 5^ X.CUT
Above 85 per cent humidity the crystal Methods for Obtaining Longitudinal, Flex-
will absorb water from the atmosphere on urali Torsional, and Pbue Shear Vibrations from an
its surface and will slowly dissolve if kept X~cut Rochelle Salt Crystal
(C) BENDER
13-66
ELECTROMECHANICAL-ACOUSTIC DETICES
In such an atmosphere. To minimize these humidity effects the crystals are often coated
with waxes, which, however, retard rather than prevent the dehydration of the crystal. If
the crystal can be hermetically sealed in a container with powdered crystalline Rochelle salt
and dehydrated Rochelle salt, it can be made to last indefinitely. The powdered salt will
give up water if the temperature rises and the dehydrated salt will take up water if the
temperature lowers, and the two will maintain a humidity that approximates the lower
curve as a function of temperature. At a temperature of 55 deg cent (130 deg fahr) the
crystal breaks up into sodium tartrate and potassium tartrate with the evolution of one
mole of water which dissolves the two crystals in a liquid solution. If this solution is
rapidly supercooled it remains quite fluid for a number of minutes before it crystallizes
and hardens. This "melted1' Rochelle salt forms a very stiff glue that has been usedjjo
glue together pieces of Rochelle salt.
VOLTS PER
CENTI METER: SOOf-J
5
O X) 20 3O 40 5O
TEMPERATURE IN DEGREES CENTIGRADE
FIG. 10. Limits of Humidity Stability of a
Rochelle Salt Crystal
-3O -2O -10 O K) 2O 3O 40
TEMPERATURE IN DEGREES CENTIGRADE
50
FIG. 11. Free Dielectric Constant of an Z-cut Rochelle
Salt Crystal as a Function of Temperature and Field
Strength
Between the temperatures of —18 and +24 deg cent Rochelle salt has ferroelectric
properties. By this is meant that it becomes spontaneously polarized in the ±x direction.
A small applied field causes a large change in polarization and one which follows a hysteresis
loop as does a ferromagnetic material. Since the piezoelectric strain is proportional to the
polarization, a large distortion of the crystal occurs. Hence Rochelle salt is principally
used when a large motion is required for a small applied voltage. The displacement, how-
ever, shows a hysteresis effect and varies considerably with temperature for a given applied
voltage. The piezoelectric equations for Rochelle salt can be written in the form
Si
-f
533^3
(11)
where in cgs units the constants have the values
su = 5.18 X 10"12 cm2 per dyne su? = 7.98 X 10"12
$n = 3.49 X KT12 sis0 = 32.8 X 10"12
, - 48 X 10~8
= -^ = 10.0
= 3.34 X IQ-&
10.08 X lO"1
, - 10.2
«u 1.53 X 10~w £U = 62 X 10-*
to = -2.11 X 10"12 £25 = 170 X 10~8
$23 - —1.03 X 10"12
For the inks system the elastic compliances are multiplied by 10, the piezoelectric constant
g is multipEed by S X 10s, and the dielectric constants are multiplied by 8.85 X 10"12.
PROPERTIES OF ROCHELLE SALT 13-67
The only constant in the above equations that varies widely with temperature and field
strength is the dielectric constant enT (the inverse of j3nT$. For low field strengths and
frequencies above 1 kc, the dielectric constant as a function of temperature is shown by
the dotted line of Fig. 11. It rises to very high values at the two Curie temperatures — 18
and +24 deg cent. For high field strengths the dielectric constant, as shown by the solid
line of Fig. 11, measured by the average slope of the hysteresis loop, becomes larger be-
tween the Curie points than it is at the Curie temperatures.
USEFUL CUTS IN ROCHELLE SALT. The cut most widely used is the X cut, which
as shown by Fig. 9(6) is cut with its major face normal to the X axis. If a voltage is applied
to this cut it shears so that the square changes into a rhombus. By cutting the crystal
length 45° from the crystallographic Y and Z axis, a crystal is obtained which elongates
along one direction and contracts along the width. This cut which is known as the 45°
X cut is widely used in producing longitudinal vibrations. By combining two longitudinal
crystals as shown by Fig. 9(c) a "bimorph" crystal is obtained which bends. This has a
much lower frequency than a longitudinal crystal and is used in voice-frequency apparatus
for picking up and reproducing sound. Figure Q(d) shows a combination of two X-cut
crystals used to produce a twisting motion. The center faces of the two crystals form one
set of electrodes and the two outside electrodes the other pair so that two opposing face
shears are applied to the combination. This causes the whole crystal to twist and produces
a torsional motion in the pair. Finally Fig. 9(e) shows two thin face shear X-eut crystals
which, when they are clamped on three corners, produce a large motion at the fourth
corner. All three of these bimorph type-crystals have been used in such devices as phono-
graph pickups, microphones, headphones, loudspeakers, surface-roughness analyzers,
and light valves and have many other applications.
For a 45° X-cut crystal the equations applicable for the extension are
Si -
(12)
Ex = -giTi -f &iT&x
where Si is the strain along the length, TI the stress applied along the length, gi the effective
piezoelectric constant for the 45° axis, and @T the impermeability (inverse of the dielectric
constant) which is measured when the crystal is free to move. In cgs units the above
constants have the values
aa'J) := 3.16 X KT12 cms per dyne; gi = 31 X 10~s - ~ (13)
while the free dielectric constant, which is the inverse of j5r, has the value shown by Fig. 11
for low applied fields and for high fields (500 volts per centimeter). Equations (12) can
be used to predict the action of the crystal under static conditions or at frequencies much
lower than the resonant frequencies of the crystal. For example, if we wish to find the
response of the crystal as a microphone, the second equation states that, for open-circuit
conditions for which the charge on the surface, and hence the electrical displacement Z>a,
is zero, the potential generated for a given pressure (negative of the tension TI) is
f
Ex = — == giTi = 31 X 10"8 (pressure in dynes per cm*) (14)
It
Since the electrostatic unit of potential, the statvolt, is 300 volts, the volts generated pear
dyne per square centimeter pressure are
^voits = 31 X 10~* X 300 X It X p = 9-10 X 10~s volt per dyne per sq. cm. for
a crystal 1 cm thick (15)
Since the voltage generated for a given pressure is directly proportional to the gi constant,
which is one-half the appropriate shear constant, eqs. (11) shows that a 45° F-cut crystal,
which will have a gi piezoelectric constant equal to lfe X 170 X 10~~8 = 85 X 10"~s, will
generate about 3 times the open-circuit voltage for the same pressure that a 45° X-cut
crystal will. The 45° Y-cut has been used to some extent as a microphone and as a trans-
ducer in underwater sound equipment for transforming electrical into mechanical energy.
When the crystal is used as a microphone working into a low impedance, the F-ctit will
not deliver as much voltage as an X-cut crystal on account of the very low impedance
(high capacity) of the X-cut crystal, but the voltage that it does deliver is not a function
of the temperature as is the voltage of the 45° X-cut.
By eliminating D* from eqs. (12), the strain Si, which is the expansion per unit length,
can be expressed in terms of the applied field as
13-68
ELECTROMECHANICAL-ACOUSTIC DEVICES
In the absence of an external stress Ti the total free displacement of 1 volt applied is
d = Sil = 1.03 X 10-9 ^ E ~ (17)
This displacement as a function of the volts per inch applied is shown by Fig. 12 for several
different temperatures. Outside the Curie region the displacement is much less since the
dielectric constant e^ is so much smaller, particularly for large fields.
When two crystals are glued together to form a bimorph unit it has been shown (see
W. P. Mason, Electromechanical Transducers and Wave Filters, p. 214, Van Nostrand) that
the displacement of the component longitudinal crystals is multiplied by the factor
3l/lt, ^where I is the length of the crystal and It the total thickness of the two elements.
This is a method of enhancing the total displacement of the unit at the expense of a con-
siderable lowering of the resonant frequency of the device. Since the dielectric constants
of the two crystals glued together will be less than the free dielectric constant of Fig. 11
and will approach the dielectric constant of the clamped crystal shown by Fig. 13, the very
400
£300
X.
VOLTS PER
CENTIMETER:
•<— 500
800
50
-3O -2O -IO 0 1O 20 3O 4O
TEMPERATURE IN DEGREES CENTIGRADE
FIG. 12. Clamped Dielectric Constant of an X-cut
Rochelle Salt Crystal as a Function of Temperature and
Field Strength
0 200 400 60O 800 tOOO
VOLTS (PEAK) PER INCH THICKNESS
FIG. 13. Strain in Rochelle Salt as a Func-
tion of Temperature and Field Strength
large temperature and saturation effects noted for the free crystal will be considerably
reduced for the bimorph type. However, the response may vary by a factor of 5 for a
wide temperature range. A typical response in the ferroelectric range for a bender unit
1 1/2 in. long, 3/4 in. ^ide, and 0.040 in. thick is
33 volts
77 volts
125 volts
140 volts
0.002 in.
0.0045 in.
0.006 in.
0.0056 in.
The displacement for any other shape unit will vary in proportion to the factor (I /It)2 and
will be independent of the width.
When such units are used as voltage generators as in phonograph pickup devices, the
mechanicaMmpedance of the device is very considerably lowered over what would be
obtained with a clamped longitudinal device. The response can be calculated by deter-
mining how much strain is generated by a given motion and calculating the voltage from,
eqs. (12) . A typical unit 0.030 in. thick, n/16 in. iongj ^d 7/16 in. ^de will give an output
as high as 1 volt when played from a phonograph record. This response will be relatively
independent of the temperature when the device is worked into the grid of a vacuum tube.
35. PROPERTIES OF AMMONIUM DIHYDROGEN
PHOSPHATE (ADP)
Ammonium dihydrogen phosphate, which has been given the abbreviation ADP, is
one member of four isomorphous salts whose dielectric properties were first investigated
by Busch (Neue Seignette Elektrica, Heh. Phys. Acta, Vol. 11, No 3 [1938]). Two members
of this group, namely, potassium dihydrogen phosphate and potassium dihydrogen
arsenate, were found to have ferroelectric effects at 121 and 91 deg absolute temperature.
Of these isomorphous crystals ADP was the crystal which had the largest piezoelectric
coupling (about 30 per cent), and it was widely used during World War II as the trans-
ducing element for underwater sound projectors and hydrophones. It appears likely
that, for devices that transform mechanical vibrations into electrical vibrations — phono-
AMMONIUM DIHYDROGEN PHOSPHATE (ABP) 13-69
graph pickups, microphones, etc. — ADP will give superior results to Rochelle salt and
may eventually replace it for such applications. For devices that have to produce a large
motion for a given voltage, however, Rochelle salt is still the only crystal that has a
large enough du constant to be of interest.
ADP crystallizes in the tetragonal scalenohedral class with the habit shown by Fig. 14.
The c or Z axis lies along the long direction of the crystal; this is an a*n's of fourfold alter-
nating symmetry. The X and 7 axes lie normal to
the prism faces; they are axes of two-fold symmetry.
Since the properties of crystals cut normal to these
two surfaces are identical it is a matter of conven-
tion which is called X and which 7. The two
diagonal axes, labeled PI and Pzt can be distinguished
by piezoelectric tests, and PI has been taken as that
axis along which a positive stress (tension) produces
a positive charge at the positive (i.e., the upper) end
of the Z axis. With the Z axis vertical and the PI
axis toward the observer's right hand, the X axis
has been taken as the axis that runs from front to
back of the crystal and the 7 axis the one that runs
from left to right.
ADP, which has the chemical formula NH-iHsPO^
has no water of crystallization and hence will not
dehydrate when the humidity becomes low. At
about 93 per cent humidity, the crystal will del-
iquesce and will pick up water from the atmos-
phere. In practice it is necessary to keep the crys-
tal in an atmosphere for which the humidity is 50
per cent or less since the water collected on the pt
surface provides a leakage path across the crystal
edges which becomes low enough to cause trouble
for humidities above 50 per cent. Owing to the hy-
drogen bond system ADP also has a volume leakage
which for a pure salt is shown by Fig. 15. For the
Z-cut crystal having a dielectric constant of 15.7
this leakage will impair the response only for fre-
quencies below 1 cycle per second. However, cer-
tain impurities introduced by the growing process
can markedly decrease this resistivity, and for some
applications it is necessary to specify a high resistivity. ADP can be taken up to ISO deg
cent before it melts. However, ammonia is given off from the surface at temperatures
above 100 deg cent, and since this impairs the adherence of the electrodes to the crystal
surface it is desirable to keep the temperature of operation under 100 deg cent. The
crystal, therefore, is useful under any likely ambient temperature conditions.
The piezoelectric equations for ADP take the form
FIG. 14. 45° Z-cut ADP Crystal and
Form of Natural Crystal
£3
4-
(18)
S*
where in cgs units the constants have the following values:
«u = 1.74 X 10~12 cm2 per dyne SUD = 11.4 X KT12 cm2 per dyne *? = 59.0
Sl2 = 0.7 X 10-12 s*P = 14.7 X 10-13 ef = 15.7
sn - - 1.1 X 10"12 £14 = 1-06 X 10-* <19)
533 = 4.35 X 10"12 gx> = HS.5 X 10~8
TTSEFtTL CUTS FOR ADP CRYSTALS. Since the gas constant is so much larger than
the £14 constant in ADP it is obvious that most of the useful cuts will be those that are
normal or nearly normal to the Z axis. A crystal cut normal to the Z axis will generate a
face shear motion similar to that shown by Fig. 9(6) for Rochelle salt. Hence by cutting
13-70
ELECTROMECHANICAL-ACOUSTIC DEVICES
the length 45° from the X and F crystallographic axes a longitudinal motion may be pro-
duced. The Z and the 45° Z cut are the principal ones used for ADP crystals. The Z cut
has been'used in'generating face shearing modes and in the production of torsional crystals.
!0IOXK>
8
6
TEMPERATURE IN DEGREES CENTIGRADE
9O 8O 70 6O 50 4O 3O 20 10 O
xto3
Z
> 0-2
i
i2 o,t
O.O6
0.04
2 CUT KDP
4-
fr
Z CUT ADP
£45
I
30
270
310
350
370
O 2 4. 6 S
THICKNESS IN MILLIMETERS
FIG. 15. Resistivity of ADP and KDP as a Function of FIG. 16. Breakdown Voltage for an
Temperature ADP Crystal as a Function of Thickness
The 45° #-cut crystal has been used as the transducing element in underwater sound equip-
ment and in microphones, in phonograph pickups, and in devices for transforming mechan-
ical energy into electrical energy.
The equations of motion of a 45° Z cut take the form
', + flg (20)
Si =
where gi = gu/2 = 59.2 X 10~8; s^P = 4.72 X 1CT12 cm2 per dyne;
*-&- 15J
When a crystal 1 cm thick is used as a voltage-generating device the number of volts gen-
erated on open circuit per dyne per square centimeter is
-Evoits = 1.78 X 1<T4 volt (21)
This is larger than for 45° X-cut Rochelle salt. On account of the lower dielectric constant
this crystal has to be worked into a higher impedance than Rochelle salt to obtain the
same output. Crystals of this sort are replacing Rochelle salt for applications such as
microphones and phonograph pickups on account of their greater chemical stability and
their ability to withstand wide temperature variations.
The electromechanical coupling factor of ADP is given by the formula
AMMONIUM DIHYDROGEN PHOSPHATE (AD?) 13-71
As can be seen from eq. (9) these crystals can convert electrical into mechanical energy,
or vice versa, efficiently over a frequency range of
7
(23)
Considerable amounts of power can be transformed from electrical into high mechanical
impedance systems. The crystal limitations are the breaking strain and the voltage
gradient that the crystals will stand. Experiments with ADP crystals show that they
will break if the strain exceeds from 4 to 10 X 10~* cm per cm. The voltage gradient
that they will stand before a voltage puncture occurs is a function of the thickness of the
crystal. Figure 16 shows the voltage gradient that will produce a puncture on the average
crystal. It can be shown that the particle velocity on the end of a quarter-wavelength or
half-wavelength crystal is equal to
| = US;* or J - 3.3 X 10*Sjf (24)
where f is the particle velocityt t> is the velocity of propagation, and SM is the maximum
strain that the crystal will suffer. This maximum strain occurs at the middle of a half-
wavelength unit or at the glued joint of a quarter-wavelength unit. Since the crystal is
stronger than most of the adhesives that can be used to attach it to high-mechanical-
impedance solid materials, the half-wavelength crystal can be used to produce more power
output than the quarter-wavelength unit. The two types of units are shown by Fig. 17.
RADIATING
FACE
METAL
QUARTER-WAVE
BACKING PLATE
QUARTER -WAVE
CRYSTAL
LOW MECHANICAL
IMPEDANCE
(3) QUARTER-WAVE TRANSDUCER (t)") HALF-WAVE TRANSDUCER
FIG. 17. Quarter- and Half-wave Transducers
The quarter-wavelength unit is glued to a heavy metal backing plate and radiates its
energy from its free face. A half-wavelength unit, on the other hand, works into a low
mechanical impedance on one end and radiates its energy from the other end. For a
half-wavelength unit the maximum strain that the crystal can safely stand is 4 X 10"*, so
that the maximum particle velocity obtainable for an ADP crystal is about
132 cm per sec
(25)
If the particle velocity is working into a high mechanical impedance such as the radiation
impedance of water, which is R X 1.5 X 10s mechanical ohms per square centimeter, the
energy radiated with this particle velocity is
£?(CTg8/sec/sQ/cm> = lm2-R — 2.6 X 10s ergs per sec per sq cm (26)
= 260 watts per sq cm
This power usually exceeds the power allowed by the voltage puncture limit (unless the
crystals are made very thin) and this is the usual crystal limitation.
It can be shown that for a half-wavelength ADP crystal radiating into a mechanical
load of RM mechanical ohms per square centimeter (ratio of force in dynes per square
centimeter to velocity in centimeters per second) the power radiated in watts per square
centimeter is given in. terms of the volt-age gradient in volts per centimeter and the mechan-
ical load jRjw by the equation
Power -
(half-wavelength radiator)
(27)
For a quarter-wavelength unit, the power radiated is one-fourth of this for the same voltage
gradient or
Power = ^J (28)
13-72 ELECTROMECHANICAL-ACOUSTIC DEVICES
Hence if we know the limiting voltage gradients, the amount of power that the crystal
will radiate before it punctures can be calculated. For example, if a half-wavelength
radiator is working into the radiation impedance of water and is made up of crystals 0.25
cm thick, the crystals should withstand a voltage gradient of 50,000 rms volts per centi-
meter. From eq. (27) the power radiated should be 660 watts per square centimeter
before dielectric breakdown occurs. Crystal fracture then becomes the limiting factor.
In practice the limitation of power does not lie with the crystal but occurs in the medium
if this is liquid or in the glued joint if a solid is used to transmit the power. A usual figure
for continuous power is 5 watts per square centimeter. If the crystal is to radiate into a
gas such as air, the limiting power is invariably determined by the limiting strain that the
crystal can stand before it breaks. From eq. (28) the maximum amount of power that
can be radiated into air by an ADP crystal is 0.075 watt per square centimeter since the
radiation impedance of air is 43 ohms per square centimeter. A crystal is not an efficient
means for exciting an air vibration.
Since the limiting particle velocity for an ADP crystal is about 130 cm per sec, a crystal
cannot be used directly to produce very high strains in metals or terminal velocities
approaching the speed of sound. If, however, a crystal mosaic is glued to a metal rod
tapered exponentially like a horn, a very high strain and a very high terminal velocity can
be produced at the small end. Figure 18 shows a construction proposed by the writer for
Y WAVELENGTH
(WHERE n=JNTEGER)
HALF-WAVE CRYSTAL
FIG. 18. Mechanical Horn for Producing a Large Strain in a Metal Sample
testing fatigue in metals. A crystal mosaic several inches in cross-section is glued to a
steel rod which tapers from the crystal area down to a thickness of 0.05 in., after which it
increases in diameter. The taper is an exponential function of the length and must
satisfy the relation
T £ ^ (29)
where the taper T is determined by the equation for the area
S
(30)
where / is the resonant frequency of the crystal, and v9 the velocity of sound in the steel.
If the total length of the steel piece is made an integral number of half wavelengths of
the frequency, the glued joint will come at a loop of the motion and will not be appreciably
strained. The whole system will act as a resonant system and will produce a considerable
motion for small applied voltages. The steel section adjacent to the crystal will have
the same particle velocity as the crystal surface. Now it can be shown that the strain in
the bar of uniform section at the nodal point (point of maximum strain) is equal to
S - f- (31)
vt
where v9 is the velocity of propagation of the wave in the steel and £ the particle velocity
at the surface. The effect of the tapered section is to increase the particle velocity in
inverse proportion to the diameter. Hence if the diameter decreases from 2 in. to 0.05 in.
the velocity is multiplied by a factor of 40 and the strain at the nodal point is equal to
S. = 40 X - S
(32)
where Sx is the strain in the steel, Sc the strain in the crystal, ve the velocity of propagation
in the crystal (3.3 X 105 cm per sec), and va the velocity of propagation in the ste^l (about
AMMONIUM DIHYDROGEN PHOSPHATE (ADP) 13-73
5.1 X 10s cm per sec). Hence, for a strain of 4 X 10~4 in the crystal, a strain of 0.01 can
be generated in the steel. This is sufficient to cause plastic deformation in the steel, and
by gradually increasing the drive on the crystal the fatigue properties of the steel can be
investigated at a high rate of strain and of velocity.
This same system can be used to produce a high particle velocity on the small end of
the steel bar. The only limitation is the strain that the metal will stand. Other uses
appear to be delivering a large amount of power for a small area. By mounting a torsional
crystal on the large end of the bar a torsional vibration can be given to the bar and the
properties of the material under shearing strain can be tested. An ADP crystal can be
made to vibrate in torsion by using the electrode system shown by Fig. 19. The inside
(a) (b)
FIG. 19. Method for Cutting an ADP Crystal to Obtain a Torsional Oscillation
surface is covered by one electrode while the two outside electrodes, each of which covers a
90° segment, are connected together and form the other electrode. The centers of the
two outside electrodes are normal to the Z axis, and the field is directed out from the
center for both electrodes as shown by Fig. 19(6), thus producing a shearing motion for
one segment and the opposite shear on the other segment so that the whole crystal is
given a torsional motion.
SECTION 14
OPTICS
GEOMETRICAL OPTICS
ABT. BY D. W. EPSTEIN PAGE
1. Reflection and Refraction 02
2. Lenses 09
3. Photometry 14
4. Light Measurement 17
5. Photometric Relations in Non-visual Op-
tical Systems IB
6. Reflective Optical System for Television
Projection 20
VISION
BY KENNETH N. OGLE
7. The Structure of the Eye 25
8. The Optical Characteristics of the Eye. 29
AST. PAGE
9. The Light Sense .............. . ..... . 30
10. Temporal Aspects of Perception ....... 33
11. Color ................. . ............. 35
12. The Space Sense ---- . ................ 39
13. Binocular Vision ..................... 46
ELECTRON OPTICS
BY D. W. EPSTEIN
14. Electrostatic Lenses .................. 51
15. Magnetosiatic Leases ................ 59
16. Electron Prisms ..................... 62
17. General Theorems on Electron Optical
Systems .......................... 63
144)1
OPTICS
GEOMETRICAL OPTICS
By B. W. Epstein
Geometrical optics is mainly concerned with the geometrical relations of the propaga-
tion of radiant energy.
Neglecting quantum effects, the propagation of radiant energy is governed by Maxwell's
equations. Fermat's principle of least time, which is the fundamental law governing the
propagation of "rays" in geometrical optics, follows from Maxwell's equations if the
wavelength of the radiation is allowed to approach zero. Although geometrical optics
applies strictly only to the propagation of radiation of zero wavelength, it provides a very
good and extremely useful approximation to any case where the wavelength is negligibly
small in comparison with the smallest linear dimension of the apparatus.
Fermat's principle of least time states that the path traversed by light in passing be-
tween two points is that which will take the least time. The general law expressed by
Fermat's principle is also known as the law of extreme path. It is stated mathematically as
0, (1)
_y = — = index of refraction.
C = velocity of radiation in vacuum.
V = velocity of radiation in medium.
dS = element of path length.
The product of index of refraction and path length, 2V dS, is known as the optical length
of a "ray of light" or optical distance. Equation (1) states that a light ray going from
point A to point B will always choose that path which will make the optical distance an
extremum (generally a minimum but sometimes a maximum) with respect to all neigh-
boring paths for rays of the same frequency. The laws of linear propagation, reflection,
and refraction may be deduced from Fermat's principle.
Although the frequency is a constant for a given radiation, and its wavelength varies
with the medium traversed, it has become customary to specify radiation, especially
visible radiation, by its wavelength in vacuum. This is due to the fact that fundamental
measurements yield wavelength rather than frequency. The units of wavelength com-
monly used hi optics are:
micron (ju) = 10~6 meter
millimicron (mju) = 10""5 meter
angstrom unit (A) = 10 ~~10 meter
The visible spectrum extends from about 0.39 to 0.75 ju; or 390 to 750 mp.; or 3900 to
7500 A; or from about 4.0 X 1C14 to 7.7 X 1014 cycles per second.
1. REFLECTION AND REFRACTION
When a beam of radiant flux or luminous flux strikes a boundary separating two homo-
geneous isotropic media, it is in general partly reflected and partly refracted. If the bound-
ary is smooth (relative to the wavelength of radiation), the following simple laws of refrac-
tion and reflection apply (see Fig. 1) .
LAW OF REFRACTION OR SWELL'S LAW. The ratio of the sine of the angle of
incidence to the sine of the angle of refraction is constant depending only on the indices of
refraction of the two media; i.e.,
ATi sin Ji = AT2 sin /* (2)
The incident ray, the refracted ray, and the normal to the surface at the point of incidence
all lie in the same plane.
14-02
REFLECTION AND REFRACTION
z a 2
14-03
PB*= REFRACTED RAY
12 = ANGLE OF REFRACTION
Nt = INDEX OF REFRACTION OF
UPPER MEDIUM
N£ = INDEX OF REFRACTION OF
LOWER MEDIUM
PQ = BOUNDARY OF TWO MEDIA
P - POINT OF INCIDENCE
AP= INCIDENT RAY
ZP= NORMAL TO SURFACE PQATP
PB= REFLECTED RAY
II = ANGLE OF INCIDENCE
lz ' ANGLE OF REFLECTION
CoJ O)
FIG. 1. Reflection and Refraction of Light Ray
LAW OF REFLECTION. The angle of reflection is equal to the angle of incidence; i.e.,
I* = -Ii (3)
The incident ray, the reflected ray, and the normal to the surface at the point of incidence
all lie in the same plane.
ijOOr
350 400 450 500 550 600 650 700
\ IN M>1
FIG. 2. Reflectance of Some Metals as a Function of Wavelength
Reflection from smooth surfaces is called specidar or regular reflection. If the boundary
is between a transparent dielectric (air, glass) and a metal, then, in general, most of the
incident flux is reflected. Figure 2 gives the specular reflectance (ratio of reflected to
incident flux) of various metals as a function of wavelength.
14-04
OPTICS
The specular reflectance r/ at tl^e boundary of two transparent dielectrics is specified
for normal incidence by Fresnel's equation:
rf
(AT2 -
A~i)2
(4)
where JVi and AT2 are the indices of refraction of the two media.
Figure 3 shows the reflectance for unpolarized light as a function of angle of incidence
for light traveling from a lower-index medium into a higher-index medium (N% > NI).
It is seen that, as the angle of incidence is
N2>N» increased, the reflectance rises gradually
at first, and then rapidly, until it becomes
unity at the angle of incidence of 90°.
The remainder of the incident flux enters
the medium of index N% at the angle of
refraction /2 given by SnelTs law, eq. (2).
The Fresnel reflection can be greatly
reduced by means of a transition layer
between the two transparent dielectrics.
For normal incidence and for a particular
wavelength, the Fresnel reflection can be
reduced to zero if, as in transmission lines,
the index of refraction of the transition
layer is N — vNiNz and the thickness of
the layer is X/4.
For light traveling from a higher-index
medium into a lower-index medium
(Nz < JVi), a similar behavior is observed
up to a certain critical angle of incidence,
the critical angle being determined by the
condition that
10* 20 30* 40* 50* 60* 70* 80"
ANGLE OF INCIDENCE IN MEDIUM
since at this angle of incidence the angle
of refraction is 90° (sin 72 = 1). For
angles of incidence greater than the criti-
cal angle, the beam is totally reflected
into the initial medium. Table 1 gives
JIG. 3. Fresnel Reflectance of Unpokrized Light as a the index of refraction and critical angle
of incidence relative to air for some solids
NI into Medium of Higher Index #2 and liquids.
Table 1. Index of Refraction and Critical Angle of Substances Relative to Air
Solids
Substance
tfD
Ic
Substance
ND
Ic
Magnesium fluoride
.38
46° 26'
Water
.334
4 8o 33'
Quartz (fused)
.458
43° 18'
Ether
.357
47° 28'
Pyrex (glass)
.474
42° 43'
Alcohol (ethyl)
364
47° 9'
Methyl methacrylate
,49
42° 9'
Glycerine ...
471
42° 50'
Potassium chloride
.49
42° 9'
Carbon bisulfide
.630
37° 51'
Canada balsam
526
40° 57'
Methylene iodide
732
35° 16'
Sodium chloride . . .
544
40° 22'
50% Methylene iodide & 50%
Polystyrene
59
38° 58'
phosphorus
1 929
31° 14'
Willemite
71
35° 47'
Calcium tungstate .......
92
31° 23'
Zinc oxide
2 05
29° 12'
Zinc $u]firip. , n , T T ,..,,, x
2.37
24° 57'
rHftTTWTwl . T T ,, t ...... x .,. v
2 417
24° 26'
Cadmium sulfide
2.52
23° 23'
Liquids, 1 5 deg cent
DIFFUSE REFLECTION, If the boundary between two media is rough, specular re-
flection can be considered to exist at a great number of small smooth areas oriented in
various directions, and the reflected energy is distributed over a wide range of angles. In
general, practical surfaces (boundaries) reflect partly specularly and partly diffusely.
REFLECTION AND REFRACTION
Figure 4 illustrates this. Pure specular reflection is shown in (a) ; part specular and part
diffuse, such as would occur at most matte surfaces, is shown in (6) ; pure or ideal diffuse
reflection is shown in (c). In perfectly diffuse reflection, the flux reflected per unit solid
angle is proportional to the cosine of the angle measured from the normal to the surface.
This statement is known
as Lambert's law. 2
DISPERSION. The
variation of the refractive
index of a substance with
the wavelength (color) of
the transmitted light is
termed dispersion. The
index of refraction of most
glasses varies with wave-
length in a manner which
may be approximated by
the dispersion formula of
Cauchy:
V
PURE SPECULAR REFLECTION
(cO
PART SPECULAR AND PART
DIFFUSE REFLECTION DISTRIBU-
TION A FUNCTION OF I,
IDEAL DIFFUSE REFLECTION
DISTRIBUTION INDEPENDEKT OF It
(C)
FIG. 4. Specular and Diffuse Reflection
The refractive index of
optical glass is generally
measured with certain defi-
nite wavelengths or lines
of the spectrum. It has
become customary to use
the spectral lines A'
(0.7665 ju) ; C (0.6563 M) ; D (0.5893 /*); F (0.4S61 AC) ; G' (0.4341 /*). The differences in
refractive index JVb — NC, N-p — JVb, NG' — JVp, JVb — N&.', and Ny — NQ are taken
as a measure of the dispersion of the glass in the different parts of the spectrum. If a
glass is specified by only one index of refraction JVb is generally meant. A quantity
related to dispersion which is in very general use utilizes the F (blue), D (yellow), and
C (red) portions of the spectrum and is designated by:
- 1
(6)
The V values, NA'» NC, ND, 7V>, and NQ'f for some Bausch & Lomb Optical Company
glasses are given in Table 2.
Table 2. Indices of Refraction and F-ntunber of Some Optical Glasses Made by Bausch
and Lomb Optical Co.
NA'
Nc
NT>
N?
NG'
tfD-l
Type of Glass
766.5 mn
656.3 rnjii
589.3 m^
486. 1 mji
434.1 HIM
r NY - Nc
Borosilicate Crown BSC-I . . .
Crown G-l
1.50578
1.51729
.50860
.52036
1.51100
1.5SSOO
.51665
. 52929
1.52114
1.53435
63.5
58.6
Light Barium Crown LBC-1 .
Dense Barium Crown DBC-1 .
Crown Flint CF-l
1.53529
1.60439
1.52217
.53842
.60793
.52560
1,54110
1.61100
1.5S860
.54746
.61832
.53584
.55257
.62421
.54178
59.9
58.8
51.6
Light Barium Flint LBF- 1 ...
Extra Light Flint ELF-1
"Barium Flint BF-2 - -
1.58110
1.55086
1 59682
.58479
,55495
.60130
1.58800
1.55850
1.60550
.59580
.56722
.61518
.60212
.57447
. 62345
53.4
45.5
43.6
Light Flint LF-I
1.56425
.56861
1.57250
. 58208
.59011
42.5
Dense Flint DF-2 ...
1 . 60684
.61218
1.61700
.62904
. 63929
36.6
Dense Barium Flint DBF- 1 . .
Extra Dense Flint EDF-3. . .
1.60731
1.70555
.61242
.71309
1.61700
1.7SOOO
.62843
.73766
.63811
.75304
38.5
29.3
REFRACTION AJTD REFLECTION AT SPHERICAL SURFACES. Because of the
relative ease of manufacture, most optical systems consist of a series of spherical surfaces,
a plane being the limiting case of a spherical surface of infinite radius of curvature. By
determining the plane containing the ray to be traced and the center of curvature, any
problem of refraction or reflection at a spherical surface may be reduced to a problem in
plane trigonometry.
14-06
OPTICS
SIGN CONVENTION. Referring to Fig. 5, let the paper represent the plane of inci-
dence containing A\Q, the ray to be traced through the refracting surface, and C the center
of curvature of the spherical surface. The signs of quantities in optical calculations have
not been standardized, but the sign convention indicated in Fig. 5 is very widely used.
FIG. 5. Refraction at a Spherical Surface
Distances measured to the right of the pole A (or center of curvature C) are positive;
those to the left of the pole A are negative. Distances above the axis are positive, and
those below the axis are negative. Angles shown clockwise are positive; those shown
counterclockwise are negative.
EXACT RAY TRACING EQUATIONS. Using the above sign convention, the stand-
ard ray tracing equations given below follow from the law of refraction and plane trig-
onometry. It is assumed that the quantities NI, Nz, R, and Si (or Pi) are given and that
Ui is assigned an arbitrary value for each ray. The problem is to find 7i, lz, C/2, and 82
(or P2).
sin /i = — ^5 — sin U\ — -~ sin Ui (7)
R
—
- r * • r
sin Ja = -r=- sin Ji
N2
Uz = Ui + I]
, - R = P2 = R
.-Is
sin Iz
sin Uz
(8)
(9)
(10)
In dealing with a complete optical system with many surfaces the results of one surface
are taken as the initial data for the next surface. The following equations which may also
be derived with the aid of Fig. 5 have been found very useful in optical calculations:
(11)
(12)
(13)
Vz sin 272 — Pi-ZVi sin I
UQ =• Ui + Ii -
h = R sin UQ
i cos Ii Nz cos Iz NZ cos Iz — NI cos I.
+ Ia
R
- COS UQ
(14)
Since at reflection Iz = — Ii, sin I* = — sin /i, the law of reflection may be treated math-
ematically as a particular ease of the law of refraction, i.e., where AT2 = — JVi. Hence the
refraction formulas given above apply to the case of reflection at a spherical surface by
simply letting N$ = —JVi. Thus for a spherical mirror, the above equations become
(Fig. 6):
•p
sin /i = — 1 sin Ui (15)
sin Is = — sin Ji
P2sin Uz
_1 1
Pi Pi
sin t/2
-Pi sin Ui
2 cos Ua
(16)
(17)
(18)
(19)
(20)
REFLECTION AND REFRACTION
14-07
FIG. 6. Reflection at a Spherical Surface
PARAXIAL FORMULAS. The exact trigonometrical formulas just given are tran-
scendental and are therefore extremely difficult to manipulate. Great simplification is
obtained if the equations are restricted to paraxial rays, i.e., rays that make small angles
with the optical axis and with the normals to the refracting and reflecting surfaces. The
paraxial formulas given below are deduced from the exact formulas by replacing the sines
of the angles by the angles and the cosines by unity. Paraxial quantities will be indicated
by the corresponding lower-ease letter:
si - R Pi /i>n
*i = — ^ — tii = -5 MI <^1)
-f- »i —
Pi
R
The corresponding equations for a spherical mirror are:
Pi
(22)
(23)
(24)
(25)
(26)
(27)
(28)
(29)
(30)
(31)
(32)
(33)
- + - = - (34)
S2 Si 5
Paraxial relations are linear and therefore are easily manipulated algebraically. They are
very useful for determining the approximate focusing action of an optical system.
If the object is at a very great distance, i.e., l/«i — 0, the image is located at the second
focal point at the distance
f^-J^—R (35)
14-08
OPTICS
to the right of the apex A. If the image is located at a very great distance, i.e., l/s2 = 0,
then the object is located at the first focal point at the distance
to the left of the apex A. For a spherical mirror
/2 = /i = f
and both focal points coincide. It should be noted that in general
fi
(36)
(37)
(38)
This relation applies to any optical system where N% is the index of refraction of the
image space and NI that of the object space.
MAGNIFICATION. The above relations suffice to locate an image of an object, but
they do not explicitly give any information about the sizes of object and image. As is
(a) MAGNIFICATION IN REFRACTIVE SYSTEMS
(Jr) MAGNIFICATION IN REFLECTIVE SYSTEM
FIG. 7. Magnification in Optical Systems
seen from the geometry of Figs. 7 (a) and 7(6), the lateral magnification which is defined
as the ratio of image height fo> to object height hi is
— £-g (39)
It is to be noted that m is negative for an inverted image (as in Fig. 7) and positive for an
erect image. Inserting (39) into (11) there result the very important relations
Ut = hiNi sin Ui (40)
Equation (40) or (41) is known as Abbe's sine condition and applies to any number of re-
fracting and reflecting coaxial surfaces (ATi index of object space, N$ index of image space).
The corresponding paraxial equations
(42)
are known as Lagrange's theorem.
(43)
LENSES
The longitudinal magnification along the axis is
Wig == " — 771
A$i
The angular magnification is
u\ m
The relation between these magnifications is
14-09
(44)
(45)
(46)
2. LENSES
By applying the above paraxial relations to a lens in air, Le., two refracting surfaces, as
shown in Fig. 8, it may be shown that the two focal points (Fi, F2) and the two principal
points (Hi, #2) completely determine the paraxial focusing characteristics of the lens.
FIG. S. Focusing Characteristics of Thick Lens in Air
The first focal point, jPi, may be considered as that object point which is focused at in-
finity in the image space so that all paraxial rays passing through the point Fi are parallel
to the axis in the image space. The second focal point, P^ may be considered the image
of an object at an infinite distance from the lens in the object space so that all paraxial
rays which are parallel to the aris in the object space will pass through F* in the image
space.
The distances indicated by /i and /i in Fig. 8 are known as the principal or equiwlenl
focal lengths and are given by
J.T J.fc 1.1*2 »
/2 " (N - l)[AT(£s - Ri) + (N - l)t] = ~h
The positions of the focal points measured from the refracting surfaces are given by
(47)
(48)
(49)
The focal distances &FI and s^2 are known as the front focal length (F.F.L.) and back focal
length (B.F.L.) respectively." These focal lengths are easily measured by imaging an
object at a great distance from the lens and noting the distance between image and nearest
surface of the lens and then turning the lens around and repeating the operation. The
positions of the principal points Hi and Hi measured from the refracting surfaces are
.given by
-MT--/.^^^- (50)
AT - 1 t
(51)
14-10 OPTICS
The distance between the principal points is
From (50) and (51) it is seen that
S^ = |l (53)
SH2 Rz
In many practical eases the lens thickness, t, is numerically small in comparison with
either Ri, RZ, or (R% — -Ki), and then
Rit Rtf
For a biconvex lens with Rz = — Ri(Ri positive)
_ Ri _ t _ t
h = 2(N - 1) SHl = 2N *Hz ~ ~ 2N
If Rz 7* RI, both principal planes move toward the surface with the higher curvature, and
when RZ = ±°°, i.e., for a plano-convex lens,
The positions of the focal and principal points of an optical system having been deter-
mined, its focusing action may be calculated with the aid of the following formulas (see
Fig. 8).
XiXz - fifz = -/a2 (56)
5-5-S (57;
mfc__A_:*«_5 (58)
til -o-l 72 *i
sz = -Mm - 1) (59)
*i- ~/2(m^ 1} (60)
THIN LENSES. A lens of negligible thickness relative to its focal length is known as
a thin lens. For a thin lens, SHI — SH% — d = t — 0, and great simplification in computa-
tion results. For a thin lens the distances si, sz, fi, and/2 in eqs. (56) to (60) are measured
from the (center of) lens, and the distance between object and image is
(61)
COMPOUND LENSES. Because of the necessity for correcting aberrations most
lenses are compound; i.e., they consist of several lenses having a common axis. Some of
the surfaces of adjacent lenses may be in contact and others are separated by air spaces.
The focal length of two thin lenses in contact of focal lengths /aa and fa is
/. = (62)
The power of a lens measured in diopters is defined as P — l/f, where / is measured in
meters. Thus the power of two thin lenses in contact is
P=*^- + ^-=Pa + Pb (63)
ha fa
If the two thin lenses are separated by an air space of thickness t, the resulting lens is
effectively a thick lens and the focal length of the combination is
, /2o/26 .
h = , . . - ; = -/i (64)
/2o + /26 — t
and the power is
P = Pa + Pb ~ tPJPl (65)
LENSES
14-11
/aa + /» -
The principal points and focal points are located at (see Fig. 9)
hat hbt
Sffi = — OET =
ha + /26 — t
SFi = /to + Afr - *
The distance between the principal points is
d
+ /26 -
(66)
(67)
FIG. 9. Focusing Characteristics of Two Thin Lenses Separated by an Air Space
There are three ways of compounding two lenses.
1. Both lenses are converging; i.e., f*a > 0 and/2& > 0. In this case the focal length of
the combination is a minirnum and the power is a maximum when t — 0. The focal length
increases as t is increased until when t — fza + f&> the focal length is infinite and the system
is afocal or telescopic. Objectives, magnifiers, and eyepieces are generally compounded
of two such lenses with t < /*a + /2&. The focal length of the combination is negative for
t > /2a + /25t and such a combination forms the compound microscope.
2. Both lenses are diverging; i.e., ft* < 0 and /2& < 0. The focal length of the com-
bination is negative and decreases in absolute values as t is increased.
3. One lens is converging /Jo > 0 and one diverging fa < 0. If | f& \ < \ f*a the focal
length of the combination is negative for values of t <\ha +f^>\, it is infinite for t
= 1 fza -h /2& [ ; this is the optical system of the Galilean telescope which produces an
erect image. The focal length is positive for t > | /^ -J- /2j j and corresponds to the opti-
cal system of a telephoto lens. If j /#, | > | /2o | the focal length is always positive.
ABERRATIONS. Actual imagery with practical lenses departs from the paraxial
or first-order imagery discussed above. These departures are known as aberrations.
There are seven independent third-order aberrations.
Spherical aberration or aperture defect is illustrated in Fig. 10. In the presence of
spherical aberration the rays from a point object on the axis do not reeombine to form a
CIRCLE OF
LEAST CONFUStON
OBJECT POINT
PARWC1AL
IMAGE POINT
EIG. 10. Positive or Undercorrected Spherical Aberration
point image as required by paraxial theory. Spherical aberration is generally measured
by the axial intersection distance, ASz, which varies approximately as the cube of the con-
vergence angle Z7i. Any simple convex lens has positive spherical aberration and is cor-
rected by compounding it with a concave lens which has negative spherical aberration.
14-12
OPTICS
In a single lens the spherical aberration is minimized if the deviation is equally divided
between the two surfaces of the lens.
Coma is an extra-axial aberration; i.e., it affects image points not on the axis of the
lens. It may be considered lateral spherical aberration for an extra-axial point. If coma
is present a point object is imaged into a comet-shaped figure. It increases directly with
the distance of the object point from the axis and as the square of the aperture of the lens.
Coma, unlike spherical aberration, may be eliminated from a single thin lens for one object
distance; however, a lens for zero coma is not the same as one for minimum spherical
aberration. Coma may be eliminated by a stop of the proper aperture located at the
proper distance from the lens. A lens corrected for spherical aberration and coma for a
given object distance is called an aplanatic lens. If spherical aberration is absent the
condition for freedom of coma is given by Abbe's sine condition, eq. (40) or (41).
Astigmatism, like coma, affects only extra-axial points. When astigmatism is present
each object point has two images, one behind the other. These images are short lines at
right angles to each other. One is called the sagittal or radial astigmatic line since it is in
a plane containing the axis of the system. The other is called the tangential or transverse
astigmatic line since it is at right angles to a line drawn from the lens axis. Midway the
two line images the cross-section of the beam is a circle of least confusion. The astig-
matism is positive if the sagittal focus is farther from the lens than the tangential focus.
Otherwise it is negative. Astigmatism increases as the square of the distance of the object
point from the axis and directly as the aperture.
Astigmatism and curvature of the field are generally present together, and the sagittal
and tangential foci lie on curved surfaces as illustrated in Fig. 11. If only curvature of
L IN
1\
IDEAL, IMAGE PLANE
S
(a) PURE CURVATURE
OF FIELD
Ct) POSITIVE ASTIGMATISM
WITH POSITIVE TANGENTIAL
AND SAGITTAL CURVATURE
(C) NEGATIVE ASTIGMATISM
WITH NEGATIVE TAN-
GENTIAL AND POSITIVE
SAGITTAL CURVATURE
FIG. 11. Astigmatism and Curvature of Field
the field is present the image points lie on a spherical surface known as the Petsval surface,
which is indicated in Fig. 11 by P.
Distortion is the variation of magnification with the distance of an object point from
the axis. Positive, or "barrel" distortion, exists if the magnification decreases with in-
creasing distance of an object point from the axis. Negative, or "pincushion," distortion
exists if the magnification increases with increasing distance of an object point from the
axis. Distortion increases as the cube of the distance of an object point from the axis.
Chromatic aberration is due to the fact that the focal length of a lens depends upon
its index of refraction and thus upon the wavelength of the light used. As a consequence
FIG. 12. Longitudinal and Lateral Chromatic Aberration
a single lens forms a series of colored images of different magnifications at different dis-
tances from the lens (Fig. 12) . The variation of image distance with wavelength is known
as kmg&todinal chromatic aberration. The difference Sac — S& is taken as a measure of
LENSES
14-13
the longitudinal aberration, and for a thin lens it is given by
1
S2C — -S2F :
(- + —
\AD
(69)
where V is given by eq. (6). The variation of image size with wavelength of refraction is
known as lateral chromatic aberration and is measured by he — ^F-
STOPS. Any obstacle which limits the rays that can be transmitted through an
optical system is a stop. Stops serve (1) to limit the aperture of any bundle of rays, and
thus the amount of light, that reaches any image point, and (2) to limit the extent of the
object which is imaged, or the field of view. The stop that limits the diameter of the bundle
of rays that can enter the optical system is called the aperture stop or iris. The stop that
limits the field of view is known as the field stop. In Fig. 13, NP is the image of AS formed
OBJECT PLANE
IMAGE PLANE
CIRCLES OF CONFUSION
OF RADIUS -a
FIG. 13. Aperture Stop, AS, and Field Stop, FSi, in an Optical System
by that part of the optical system Gens I/i) situated between AS and the object. Since
NP limits the angular aperture Ui of the beam, AS is the aperture stop. NP is known as
the entrance pupil. If an actual stop were located at NP instead of AS, then the iris and
entrance pupil would coincide. The image XP of AS formed by that part of the optical
system (lens L*) situated between AS and the image is known as the exit pupil. The
angle subtended by the object at the center of the entrance pupil is known as the angular
field of view of the object. In
Fig. 13 the angular field of view
of the object is limited to 21^1
by the aperture stop FSi. If
it is desirable to have a sharp
boundary of the field of view
it is necessary to have FSi in
the plane of the object.
Stops play a very important
role in eliminating those rays
that would produce excessive
aberrations.
DEPTH OF FOCUS. The
maximum total distance, A&2,
that a viewing screen may be
moved along the axis of an
optical system to produce a
circle of confusion of prescribed
radius, r, is called the depth of
focus (Fig. 14a) . It is given by
4x) DEPTH OF FOCUS
CIRCLE OF CONFUSION
OF RADIUS yv
t=*2r— = 2rcot C72 (70)
(ti DEPTH OF FIELD
FIG. 14. Difference between Depth of Field and Depth, of Focus
where Sz is the image distance,
at best focus, measured from
the exit pupil of radius a,$.
DEPTH OF FIELD. The maximum total distance, ASi, that an object may be moved
along the axis to produce, at a fixed image distance, a circle of confusion of prescribed
radius, r, is called the depth of field (Fig. 146). It is given by
_•*
-f-
(71)
14-14
OPTICS
where m is the magnification and Si is the object distance, at best focus, measured from
the entrance pupil of radius a\. If r <$C mai, then
ASi « 2 - —
2 - cot
(72)
3. PHOTOMETRY
The problem in photometry is to obtain a quantitative evaluation of radiant flux with
respect to its capacity to produce the sensation of brightness. The sensation of brightness
evoked by a given amount of radiant energy is different for different individuals and is
different for the same individual under different conditions of observation. Equal amounts
of radiant energy per unit wavelength interval throughout the visible spectrum do not
produce visual sensations of equal brightness. A luminosity curve shows as ordinates
the relative effectiveness of various wavelengths to evoke, for a particular observer,
visual sensations of equal brightness. Figure 15 shows two luminosity curves applying to
t.O
? 0.8
0.7
0.6
>
< 0.5
0.4
C 03
02
0.1
I
\
\
\
A
\
380 400 420 440 440 48O 500 520 540 560 580 600 620 640 660 680 700 720 740
X IK MILLIMICRONS
FIG. 15. Curve (a), Standard Luminosity Function, Applying to Normal Vision with Good Lighting
Conditions; Curve (&), Luminosity Function Applying to Vision at Very Low Light Levels
photopic or normal vision (at high light levels) and to scotopic vision (at very low light
levels). These are average luminosity curves obtained for a number of observers. The
use of many luminosity curves would, obviously, lead to endless confusion and ambiguity
in photometric measurements and specification. To avoid this, the International Com-
mission on Illumination adopted Fig. 15a as the standard luminosity curve. It is important
to realize that the standard luminosity curve is essentially an arbitrarily assumed standard
for purposes of standardization and specification of photometric data and is not neces-
sarily the retinal response of any individual. Table 3 gives the standard luminosity func-
tion, y(\) of Fig. I5at at 10-millimicron intervals.
Table 3. Standard Luminosity Function 1
X in m/i
Z/(X)
X in m/t
PCX)
Xin mjt
PCX)
X in mjt
»(X)
380
0.0000
480
0.139
580
0.870
680
0.0170
390
.0001
490
.208
590
.757
690
.0082
400
.0004
500
.323
600
.631
700
.0041
410
.0012
510
.503
610
.503
710
.0021
420
.0040
520
.710
620
.381
720
.0010
430
.0116
530
.862
630
.265
730 •
.0005
440
.0230
540
.954
640
.175
740
.0003
450
.0380
550
.995
650
.107
750
.0001
460
.0600
560
.995
660
.061
760
.0001
470
.0910
570
.952
670
.032
PHOTOMETRY
14-15
Table 4 gives the names, symbols, and basic mks units of radiometry and photometry
as recommended by the committee on colorimetry of the Optical Society of America.
The term "luminance" hi Table 5 replaces the older term "brightness" which led to con-
fusion between the objective concept of brightness as a measurable quantity and the sub-
jective concept of brightness which refers to the sensation in the consciousness of the
human observer. It is recommended that the term "brightness" be used only in the latter
sense.
* Table 4
Radiometry
Photometry
Name
Sym-
bol
Unit MKS
Name
Sym-
bol
Unit MKS
]R^.Hi?mt energy
U
P
W
J
N
H
Joule
Watt
Watt/m2
Watt'w (steradian)
Watt "wxm2
Watt/m2
Luminous energy
TAirninous flux
Q
F
\
B
E
Talbot
Lumen
Lumen ms
Lumen e* (candle)
Lumen Wxm2
(candle m*)
Lumen 7m2 flux)
Radiant flux
Radiant emittance. . .
Radiant intensity
Radiance
Luminous emittanee. .
Luminous intensity . . .
Luminance
Irradiance
TH«minfl.nee
The ratio of any photometric quantity to the corresponding radiometric quantity in
Table 5 is equal to the absolute luminosity or luminous efficiency (generally expressed as
lumens per watt) of the radiant energy. Thus 1 watt of monochromatic radiant flux of
wavelength 555 mju (corresponding to the peak of the standard luminosity curve) is
equivalent to 685 lumens. This efficiency of 685 lumens per watt is based on the fact that
the new proposed international photometric standard of a black body at the temperature
(2043.8 deg K) of freezing platinum shall have a luminance of 6 X 10* candies per m*
(60 candles per cm2).
Table 5. Conversion Factors for Units of Dltuninance
Multiply'
Number
to
Obtain
Lux
Foot-candle
Phot:
Mffliphot
Lumen/m2 Lux ,
Lumen/ft2 Foot-candle.
Lumen/cm2 Phot
MilHphot. . .
0.0929
0.0001
. 1
10.76
0.001076
1.076
10,000
929
I
1,000
10
0.929
0.001
1
If the radiant flux is monochromatic its luminous efficiency is simply 6&5£(X). If the
radiant flux is not monochromatic but consists of a continuous spectrum, then if P(X) is the
radiant flux per unit wavelength (watts per millimicron) the luminous efficiency is
dX
685-
(73)
Luminous efficiency should not be confused with the efficiency of a practical light
source, which is the ratio of the total luminous flux to the total power input. The effi-
ciency of a source of light is less than K since generally a fraction of the total power input
is not converted into radiant flux.
LUMINOUS INTENSITY OR CANBLEPOWER OF A SOURCE. By a source win
be understood (a) any self-luminous object, such as an incandescent body, or (6) any
illuminated object which so completely diffuses (either by reflection or transmission) the
incident light that it acts as a source.
The intensity of a source is defined as
I = *? (74)
and is measured in lumens per steradian, or candles. In Fig. 16, let the small plane source
14-16
OPTICS
of area A0 emit P watts or F - 685 /*°°£(X)P(X) d\ lumens. The two small -receivers of
•'O
areas Al and A2 subtend the same solid angle Aco at the (say, center of) source and are
located at the same distance D from the source. The number of lumens AFi and AF2
contained in the same solid angle Aco will, in general be different. Thus the intensity
— — - , is not equal to the intensity, /« = -r— , measured along
AOJ ™ **•
normal to the source, 70
AF2
Aco ^
a direction at the angle a.
with the normal. In specify-
ing the intensity or candle-
power of a source, it is there-
fore necessary to state the
direction in which the inten-
sity was measured or give
a candlepower distribution
curve. The directional char-
acteristic of many extended
sources follow Lambert's law,
which states that
Ia s* Jo cos a. (75)
With a uniform point or
spherical source, the inten-
sity is independent of direc-
tion and is F/4ir. Thus a
uniform point or spherical
source of an intensity of 1
candle emits 4?r lumens.
ILLUMINANCE. A surface of area dA, placed in a field of flux, is illuminated with
the illuminance
jn
E — -— (lumens per m2 in mks units) (76)
dA
where dF is the flux incident on the surface. The illuminance of receiver A\ (Fig. 16) is
AP, JoAco Jo (Ai cos 0) IQ
(77 a)
FIG. 16. Diagram Illustrating Some Photometric Concepts
The illuminance of receiver A 2 is
, = —z cos 0 — — cos a. cos 0
In normal incidence
(776)
(78)
which is the well-known inverse-square law. The inverse-square law, which is the basis
of most visual photometers, applies to large extended sources, if D is considerably larger
than the extension of the source. Thus (78) holds to within about 1 per cent if D is at
least 5 times the greatest linear dimension of the source.
LUMINANCE. The luminance, B, of the surface AQ (Fig. 16) in any direction is the
ratio of the intensity Ia in that direction to the area of the projection of AQ on a plane
perpendicular to the direction, i.e.,
(79)
^-0 COS Oi
Luminance is measured in candles per square meter in mks units. If Lambert's law is
followed, then
s = 4°J21£ . Jj _ Bo (so)
AQ COS CX. AQ
and the luminance of a surface is independent of a. The brightness sensation when ob-
serving a surface, whether self-luminous (as the luminescent screen of a cathode-ray tube)
or diffusely transmitting or reflecting (as a television or movie projection screen), depends
upon the luminance of the surface. Hence if the surface obeys Lambert's law, its lumi-
nance is the same in all directions, and it will appear equally bright from whatever angle
it is viewed.
LIGHT MEASUREMENT
14-17
LUMINOUS EMITTANCE. The luminous emittanee, L, of a surface is the total
luminous flux emitted per unit of area, or
i - | (8D
Luminous emittanee is measure in lumens per square meter in mks units.
The luminous emittanee of a surface obeying Lambert's Jair is found to be
L = icB (82)
Hence a perfectly diffusing (emitting, transmitting, or reflecting) surface, whose luminance
is B candles per square meter has a luminous emittanee of xB lumens per square meter.
Or a perfectly diffusing surface of luminance B and area A emits
(83)
F « TrBA lumens
If the surface radiates on both sides with luminance B, then
F = 2TBA (84)
PHOTOMETRIC UNITS. Equation (82) is the basis for another unit of luminance
called meter-lambert. By definition 1 meter-Lambert is the luminance of a perfectly dif-
fusing surface emitting, reflecting, or transmitting, 1 lumen per m2. Thus 1 meter4ambert
equals 1/x candle /m2. This unit (meter-lambert) is very convenient when dealing with
non-self-luminous surfaces such as perfectly diffusing (transmitting or reflecting) surfaces.
If these surfaces do not absorb any light, the number of lumens incident on them is equal
to the number of lumens transmitted or reflected. Hence the illuminance in lumens per
square meter, the luminous emittanee ia kirnens per square meter, and the luminance in
meter-lamberts are all numerically equal. If these surfaces do absorb some light, the
luminance in meter-lamberts is equal to the iUuminance in lumens per square meter
multiplied by the fraction of the incident light that is transmitted or reflected. The
luminous emittanee in lumens per square meter is still equal to the luminance in meter-
lamberts. If the surface does not obey Lambert's law its luminance depends upon the
angle of observation and the advantage of this unit disappears. The luminance of such
a surface in a particular direction in meter-lamberts may then be interpreted as the mim-
ber of lumens per square meter that a perfectly diffusing surface of the same luminance
would radiate.
Besides the mks units given above, there are many others in widespread use. They
differ from the mks units only in being based on different units of area. Tables 5 and 6
give the names and the relative magnitudes of the more common units of illuminance and
luminance.
Table 6. Conversion Factors for Units of Luminance
Multiply
^N, JS^
Foot-
>v ^S.
Candfe
Candle
Candle
Candle
Miffi-
lambert
Meter-
X>Os.
per
per
per ft2
per
Lambert
kmbert
(equivaieat
binbert
cm
m.2
m2
fatir
Obtain ^o^
4- *
candk)
Candle per cm2 (Stilb)
1
0.1550 ;
0.0010764
!Q-«
0.3183
0.0003183
0.0003426
0.00003183
Candle per in.2
6.452
I
0.006944
6.452
2.054
0.002054
0.00221
6.0032054
xw-*
Candle per ft2
929
144
I
0.0929
295.7
0.29^
0.3183
0.02957
Candle per m2 ....
10,000
1,550
^10.764
1
3,183
3.183
3.426
0.3183
Lambert (cm4ambert)
3.142
0.4869
3.382
3.142
1
0.001
0.001076
XIQ-*
xw~4
MilHlambert
3,142
486.9
3.382
0.3142
1,000
I
1.0764
O.I
Foot-lamberfc
2,919
452.4
3.142
0.2919
929
0.929
0.0929
Meter-lambert
31,420
4,869
33.82
3.142
10*
10
10.76
I
4. LIGHT MEASUREMENT
The methods of light measurement may be divided into two classes; visual photometry
and physical photometry.
In visual photometry the human eye is the detector. Although the human eye is
incapable of measuring, it is capable of fairly accurately judging the equality of lumi-
nances of adjacent areas. In a visual photometer, two adjacent areas of a screen are
14-18
OPTICS
illuminated by a calibrated source and an unknown source. The observer adjusts the
illuminance on the half-field produced by the calibrated source (by varying the distance
between source and screen) until he judges the two half-fields to be equally "bright."
The better visual photometers (such as the "Macbeth Illuminometer") use a Lummer
Brodhun cube to split the field. Relatively accurate measurements may be made with
visual photometers only if the spectral distribution of the calibrated and unknown sources
are approximately the same. Although a series of niters may relieve this situation, meas-
urements upon sources of different colors (heterchromatic photometry) are generally
subject to great errors unless a flicker photometer is used.
In physical photometry, the detector is generally a photovoltaic or photoemissive cell.
A cell will give true photometric values regardless of the color of the light if corrected
with a suitable filter, so that its sensitivity throughout the spectrum is proportional to
the luminosity curve of Fig. 15a. The most important error in physical photometry is
generally due to the difference between the spectral response of the cell and the standard
luminosity curve. Other errors arise from the directional and temperature characteristics
of cells. Most commercial light measurements are now made using a photovoltaic cell
with an "eye"-corrected filter.
5. PHOTOMETRIC RELATIONS IN NON-VISUAL OPTICAL
SYSTEMS
One of the important performance characteristics of an optical system is its light-
gathering power. In Fig. 17 Ihe small object of area AI radiates in all directions, but the
FIG. 17. Diagram Illustrating Some Photometric Relations in Optical Systems
lens accepts and focuses only a fraction of the flux on the image of Area A%. If A\ emits
according to Lambert's law, then the fraction of the flux that the lens accepts is
e = sin2 Ui (85)
where U\ is the angle subtended by the radius of the entrance pupil at A\. The quantity e
might be called the (geometric) efficiency of the optical system. If B i is the luminance of
A\j then the total flux, F, that A\ emits is irBiA\ and the flux accepted by the lens is
Fi = vBiAi sin2 Ui (86)
If the lens has no losses, FI is the flux that will reach the image. If there are losses in the
optical system, let k be the fraction of the incident light that it transmits, and
Fz = kFi = irBiAik sin2 Ui (87)
The quantity fc sin2 Ui might be called the effective efficiency of the optical system.
The illuminance of the image is
ik sin2
A*
m?
ik sin2 Uz
(88)
This equation is the basic relation giving the flux density on a small area (.4.2 in. Fig. 7) of
the image, located on the axis of an aplanatic optical system, produced by an extended
source emitting according to Lambert's law.
PHOTOMETRIC RELATIONS
14-19
.8
7
\
.5
\
I
1- .2
Z
U- *Q
\
>
\
_. .07
o -06
u- .05
z *04
3 .03
u.
0 .OZ
o
Z
£I007
tt.006
^ .OO5
«>.004
•OOS
.002
\
\
\
\
\
\
L
\
\
\
\
a .2 .3 .4 -S . 6,7.83 UO 2 3 4- 5 678<UO »
FIG. 18. Efficiency of a Lens Used for Projection at Infinite Tnrow as a Function of F/Number
Most lenses are rated (as to their light-gathering power) by
1
and sometimes by
//number =/n- =
Relative aperture — R A — —
(89)
(90)
Microscope objectives are rated by
Numerical aperture = NA — Nj. sin Ui (91)
If the entrance and exit pupils coincide with the principal planes of the optical system,
eq. (88) may be written
}& S-j? irBi - \RA} /oo\
•nt i> j» i_ == I- \*>-£)
j£z - fjstf ^ + ^ ^ 4 K (m2/4) (22^)2 + (m - l)s
For camera and telescope objectives, the object distance, Si, is usually very large and the
image distance, Sj, is approximately equal to the focal length (or m ^ 0) so
«£?! JL (93)
If the relative aperture is small or //number large, then for any magnification
For high-efficiency projection systems, it is preferable to define //number as
1
(95)
14-20
OPTICS
instead of eq. (89). For values of U/ less than about 10°, sin C7> - tan Uf and the two
definitions agree, but they disagree for larger values of £//. The efficiency of a projection
lens for infinite throw is thus
0 25
eM = sin2 Uf = T^T. (96)
For a lens immersed in air, the smallest FN possible is 0.5, since then the efficiency is
unity, and all the light emitted is accepted by the lens. For a lens immersed in a medium
of index NI the efficiency is e^ = NJ sin2 Uf and the FN is ;— — • • • . Figure 18 shows
the efficiency ex of a lens as a function of //number. It is seen that the efficiency of most
lenses is very low.
The efficiency of a given optical system decreases when the magnification or throw
decreases. The efficiency at a magnification ra is
7)2 *
. °°
1 + (1 -
c1
- 2m
Thus an ordinary lens with an FN of 2 has an ««, of 6.25 per cent and an em of about 4.6
per cent when used at a magnification of — 6. Similarly a lens with an e^ of 25 per cent
(FN = 1) will have an efficiency of 19.6 per cent at a magnification of — 6.
The illuminance of an extra-axial area (Awt Fig. 17) produced with a lens of small
aperture is approximately given by
*•- 2* «***£=& (98)
•where w is the field angle (see Fig. 17) .
6. REFLECTIVE OPTICAL SYSTEM FOR TELEVISION PROJECTION
Two important requirements of an optical system for television projection are: (1) that
it be capable of focusing a large field (large tube face) and (2) that it have high efficiency.
The need for a large field is that, owing to current saturation and heating of the luminescent
screen, the light output from a cathode-ray tube increases with the size of the tube, for a
given beam power input.
The most efficient optical systems capable of focusing considerable fields are, in general,
of the reflective type. One of the simplest (and best) of these consists of a spherical mirror
and an aspherical aberration-correcting lens located at the center of curvature of the
mirror (Fig. 19).
.FRONT FACE
SPHERICAL
MIRROR
FIG. 19. Reflective Optical System for Television Projection
The aberrations of any optical system with a high geometrical efficiency can be suffi-
ciently corrected for only one position of object and image. As a result a given system is
good for only a small range of magnification, and different systems have to be designed for
REFLECTIVE OPTICAL SYSTEM
14-21
different magnifications or throws. A highly efficient system has, because of the large
convergence angles, relatively shallow depth of focus and depth of field; see eos. (70) and
FOCUSING WITH MIRROR ANB CORRECTING LENS. Because of the symmetry
of tne spnere, an optical system consisting of a spherical mirror and a small aperture looted
at the center of curvature of the sphere suffers from only two aberrations: spherical aber-
ration which is uniform all over the field, and curvature of the field. With large apertures,
extra-axial aberrations of higher order enter the field, but they are not too large (see
Fig. 20).
The purpose of the correcting lens is to correct for the spherical aberration of the mirror
without introducing any serious aberrations of itself. This is accomplished by making
FIG. 20. Image Properties of System Consisting of Spherical Mirror and Aperture Located at Center
of Curvature
the lens as weak as possible and locating it in the plane of the aperture at the center of
curvature. In this way the symmetry property of the spherical mirror is least disturbed.
The curvature of the field is not corrected as it is actually used to good advantage in
cathode-ray-tube projection.
Equation (20) may be written
JL+ I=_
Pi PS xt JUQ
where /Z70 is the focal length of a zone of the mirror of aperture sin U&. The zonal focal
length fu0 thus increases with the aperture of the zone.
The spherical aberration of the mirror may be interpreted as focusing by means of
zones, each zone having a different focal length. The correcting lens has to be such that
each zone of the lens has a different focal length, compensating for the various focal lengths
of the mirror and resulting in a focusing system with all zones of the same focal length.
The shape of the correcting lens will thus depend upon the zonal focal length of the
mirror one chooses as the focal length of the optical system (mirror plus correcting lens).
Since theoretically there are an infinite number of zones on the mirror, there are theo-
retically an infinite number of correcting lens shapes that will produce a system in which
all zones have the same focal length,
Since the mirror with an aperture at the center of curvature has no extra-axial or chro-
matic aberrations, such aberrations are caused by the correcting lens itself, i.e., by the
power or slopes on the correcting lens. From the standpoint of these aberrations, there-
fore, that shape should be chosen whose maximum slope is the least. Thus if the paraxial
(central) focal length of the mirror is chosen as that of the system, then the central focal
length of the correcting lens is infinite and the shape of the curve is concave. If a zonal
focal length of the mirror is chosen as that of the system there will be a zonal focal length
of the correcting lens which is infinite and the shape of the curve is convex at the ce&ter
14-22
OPTICS
and concave past this zone. If a peripheral focal length is chosen, the required correcting
lens is convex. The maximum slope is least for a convex-flat-concave curve.
The shape of the correcting lens must be such that all rays emanating from an object
point 0i, and reflected by the mirror, shall meet at the image point Oi located at a dis-
tance S from the correcting lens. Figure 21 shows three rays emanating from Oi and
REFERENCE
ZOME
-MIRROR
SINE U0
FIG. 21. Diagram Illustrating the Effect of the Correcting Lens
striking the mirror at different apertures. Without the presence of the correcting lens,
rays 1, 2, 3 would intersect the axis at distances Pz, Pz, and P^ from the center of curvature.
The slopes on the correcting lens have to be such (approximately as shown on Fig. 21)
that all three rays intersect at Oa; hence, the correcting lens has a flat zone at the point
where ray 2' passes, negative slope where ray 1' passes, and positive slope where ray 3'
passes.
From the point of view of spherical aberration, if the zone where ray 2 strikes the mirror
is taken as a reference, then the mirror has negative spherical aberration for smaller aper-
tures and thus requires a positive lens for correction, and positive spherical aberration for
larger apertures and thus requires a negative lens.
ZONE HAVING
FOCAL LENGTH
OF SYSTEM
CORRECTOR FOR HIGH MAGNIFICATION
FIG. 22. Diagram Showing Why the Aperture of the Correcting Lens Depends upon Magnification
The shape and size of the correcting lens depend upon the throw or magnification for
which the system is to be used. For a given focal length and relative aperture the cor-
recting lens aperture decreases as the magnification decreases (see Fig. 22). That this
must be so may, be surmised from the fact that for unity magnification the lens aperture
object and image coincide at the center of curvature. Figure 23 shows the
REFLECTIVE OPTICAL SYSTEM
14-23
variation of correcting lens semiaperture and mirror semiaperture, with magnification,
for a system of given focal length and efficiency. All distances in Fig. 23 are measured in
terms of the radius of curvature of the mirror; i.e., the radius of curvature is taken as the
unit of length.
The focal length of the complete optical system depends upon the shape of the correcting
lens. In general, the higher the efficiency for which a system is designed the greater the
focal length (in terms of R). Thus for an extremely inefficient system (requiring only a
small aperture at the center of curvature and no correcting lens) the focal length would
<£~-.456
<
I
u
w
\
1
Acm
km
1 111 i i
=SEM1 APERTURE OF CORRECTING
X « » W B
- * " H MIRROR FOR
LENS [
• MINIMU1
AXIAL POf NT
ttJSHWUM RAY =.3.
u
317=
^
\
= SI
N Uc
! f I
X
X
x
V
**-
• „,
.*•
• — j
.1
— —
^. —
.. •
— -
_-
•»
» . •
_
L
y,
'
'
,'
"""
/
/
/
I/
\ Z 3 4 567*9 tO 2 3 4 56789 100 Z 3 4 i «7 491000
m
FIG. 23. Variation of Semi-aperture of Mirror and Correcting Lens with Magnification
be 0.522, whereas a reasonably good design of a system with an efficiency of about 50 per
cent (requiring a correcting lens) will have a focal length of about 0.53B.
Relations between the throw 5, magnification m, object distance Pjy and the focal length
/aie: fl-** (100)
PI = /(m + 1) (ioi)
-- /(m + 1)
(102)
Thus for a magnification of — 6 (inverted image) and a focal length of 0-5372 the throw is
2.65jR. In the reflective optical systems contemplated for home television projection re-
ceivers R = 13.7 in., and so for a magnification of — 6 the throw would be 2.65 X 13.7 in.
= 36.3 in.
TUBE FACE. Before striking the spherical mirror, the light emitted by the lumi-
nescent screen of the cathode-ray tube first passes through a thickness (generally about
1/8 in.) of glass constituting the tube face. The tube face should preferably consist of two
concentric surfaces, and thus it acts as a weak lens. The radius of curvature of the outer
surface (for a thin tube face) is approximately equal to the focal length of the system.
The lens action of the tube face changes the magnification of the system to
M
- i
(103)
N
where N, t, and RI are the index of refraction, thickness, and radius of curvature of the
outer surface of the tube face. However, the largest effect of the tube face is caused by
14-26
OPTICS
images cannot be seen. The blind spot is roughly elliptical, the vertical dimension being
longer. Its size varies greatly among individuals, with limits for horizontal dimensions
of 3 to 8 degrees, averaging about 6 degrees. The nearest edge is located about 12 degrees
on the nasal side of each retina.
Contrary to other sense organs, the entire nerve system leading to the cortical regions
of the brain is found essentially in the retina itself. Here some of the functions may occur
which usually take place in the cortex, for example the color-analyzing processes (Polyak).
THE REFRACTIVE MEDIA. The transparent intraocular fluids in all parts of the
eye are derived from the blood and physiologically are essentially the same. The fluid in
64
72
40
Age, Years
FIG. 2. The Loss of Accommodation, with Age. Data from over 4200 Eyes. (Duane, Am* J. Ophth.)
the anterior chamber (Fig. 1), called the aqueous humor, is only slightly more viscous
than water, is subject to thermal currents, and is quickly replenished if lost. The larger
chamber behind the crystalline lens is filled with a jellylike substance called the vitreous
body. This body is a combination of a protein colloid and the intraocular fluid, also per-
meated by a fine meshwork of fibrils that gives the mass a stable anatomical structure.
The crystalline lens is a transparent body having the shape of a biconvex lens, and it
serves the same function as a lens. It consists of a non-homogeneous elastic substance
made up of a number of layers or laminae, each with increasing density and increasing
index of refraction toward the core at the center. By the action of the ciliary body, through
a complex process, the lens may become more convex and in so doing serves the function
of changing the position of the focal point of the light entering the eye. In this way, the
eye can accommodate itself from distinct vision of distant objects to that of nearer ob-
jects, and vice versa. In this act of accommodation primarily the radius of the front
surface decreases and the thickness of the lens increases.
THE STRTJCTUBE OF THE EYE
14-27
-7 -6 —5
-3 -2 -1 O
Log Held Luminosity, ml
With increasing age the average density of the lens increases; the lens becomes harder
and less elastic and hence its accommodative function is less and less effective. The loss
of accommodation with age is illustrated in Fig. 2 (Duane), where the nearest distance
from the eye at which a test object remains clear is plotted against age. It is clear thatf
at about the age of 60 years, little or no accommodation remains, and the eye is then said
to be completely presbyopic.
THE PUPIL. The pupil acts as the stop or aperture of the eye. It is in a constant
state of activity and is subject to a number of reflexes. Although the pupil will contract
when the iris is stimulated directly by light, normally it contracts through a light stimula-
tion of the retina, the extent de-
pending on the adaptation of the 8 f
eye. The pupillary response to
light falling on the central part of
the retina is much greater than
for that falling on the peripheral
parts of the retina. The thresh-
old for pupillary response of the
central region of the retina, when
dark adapted, corresponds quite
well to the threshold of cone
vision. Data showing the change
in the diameter of the pupil in
response to the luminosity of an
extended surface are illustrated
in Fig. 3 (Reeves). Theoretically
the amount of light entering the
eye would be approximately pro-
portional to the area of the pupil
(diameter squared), but it is evi-
dent from the figure that, whereas
the illumination change is more than several million times, the amount of light entering
the eye changes only about 15 fold. The contraction of the pupil cannot, therefore,
even approximately [compensate for increasing illumination. The rate of contraction of
the pupil from darkness to light is much greater than the rate of dilation resulting from
light to darkness. The response of the pupil to colored light is greater for yellow than for
red or blue.
In this connection, it has been shown (Stiles and Crawford) that the intensity of the
light falling upon the retina is not directly proportional to the pupil area. Rays entering
the pupil near the edge
1-20, — , — i — | — , — | — i — , — | — , — i — j — i — , — , — i — , — j — , — , — , are much less effective
in producing a sensation
than those entering the
center of the pupil. The
relative effectiveness of
the different pupillary
zones is shown in Fig. 4.
The pupil of the eye
contracts when the eyes
are converged and ac-
commodated for near ob-
jects. This assoeisiiQfi
is more closely related to
convergence of thte eyes
than to aca»mm<>datiQa.
The refer takes place in.
addition to efctaages in
pupilary reaction doe to
changes in illumination.
FIG. 3. The Relation between Papillary Si*e and the Lu-
minosity of the Visual Field. (Data of Ree-res, J. Optical Sac.
Am.)
1.00
0.80
fcO.60
0.20
_S^
o Horizontal traverse'
• Verifca! traverse ;
543210 12345
Distance from Center of Pupil, mm
FIG. 4. Data Showing the Stiles-Crawford Effect. Light through periph- „„„_„ ^
eral zones of the pupil is less effective than that through the center. T~T^ +-„
(From Moon, Scientific Bases of IUuminatinS Engineering.) Automatic
of the pupil for near ob-
jects increases the depth of focus of the eye, where an increased depth is useful. Under
normal conditions pupillary action takes place nearly equally in the two eyes, even if only
one eye is subjected to iSumination changes. The pupil is also influenced by psychic
factors; a dilation is usually the rule, except when the individual is in a comatose state.
There is some evidence that pupillary contraction can be conditioned.
14-28 OPTICS
SCHEMATIC EYE. Because of the non-homogeneity of the crystalline lens, and the
general asymmetry of the optical elements, a schematic eye can be only an approximation
to the living eye. Frequently, however, such a schematic eye is useful for reference and
for optical problems. The data utilized by Gullstrand for the relaxed eye are given in
Table 1. The greater part of the refractive power of the eye is due to the cornea (43
diopters), the lens contributing only 1/3 of the total power. Since the distance of the
second focal point from the second nodal point of the schematized eye is about 17 mm,
an object subtending an angle of 1 minute of arc will subtend a linear distance on the retina
of 5 AC (0.005 mm) . In problems where the image on the retina must be considered blurred,
it is convenient to know the approximate positions of the entrance and exit pupils. All
optical imagery calculations can be referred to those positions if the magnification of the
two stops are known. The center of the blurred image on the retina may, for practical
purposes, be taken as the point of maximum light intensity.
Table 1. The Gullstrand Schematic Eye Relaxed for Distant Vision
Position of surfaces
Cornea, anterior surface 0.0 mm
Cornea, posterior surface 0.5
Lens, anterior surface 3.6
Core, anterior surface 4 . 15
Core, posterior surface 6.56
Lens, posterior surface 7.2
Radii of curvature
Cornea, anterior surface 7.7 mm
Cornea, posterior surface 6.8
Lens, anterior surface 10 . 0
Core, anterior surface 7.91
Core, posterior surface — 5 . 76
Lens, posterior surface — 6.0
Refractive indices
Cornea 1 .376 mm
Aqueous and vitreous humors 1 . 336
Outer portion of lens 1 . 386
Core 1 .406
Complete Optical System of the Eye
Position of first principal point 1 . 35 mm
Second principal point 1 . 60
First nodal point 7 . 08
Second nodal point 7.33
Anterior focal length — 17 . 05
Posterior focal length 22 . 78
Refractive power of eye 58 . 64 diopters
Position of entrance pupil from cornea 2.0 mm
Position of exit pupil from posterior surface of crystalline lens 3.7
Magnification of exit to entrance pupils 0 . 923
EYE MOVEMENTS. The rotary movements of each eye are controlled by six (ex-
trinsic) muscles; the opposing external and internal recti muscles which provide move-
ments for looking to the right and left; the superior and inferior opposing re cti-muscles
which provide movements for looking upwards and downwards; and the two oblique mus-
cles which provide torsional movements about the axes of fixation, as well as movements
opposing the recti in certain eye positions. The innervations to the muscles for movements
of the two eyes are said to be reciprocal in that a given movement will result from the con-
traction of one muscle and the relaxation of its antagonist. There is, therefore, a precise
coordination of the muscles that leads to very delicate and accurate movements of the
eyes. In general it can be said that the ocular movements are for the purpose of directing
the eyes to the object of attention and preventing diplopia (double vision). The move-
ments seem, essentially, to be reflex movements following the direction of attention and
accordingly have been called psycho-optical reflexes. Because the actual movements of
the eyes from one point in the visual field to another appear to be approximately correct,
it has been assumed that the retinal elements have "motor values," differences in which
lead to correct innervations for eye movements. The reaction time between the atten-
tion and the beginning of the eye movement, though varying with circumstances, aver-
ages between 0.17 and 0.20 sec.
Owing to the constant tonus of the muscles, the eyes are in a continuous state of activity.
Thus, even with constant fixation, there are occasional large, jerky movements that aver-
age 4 minutes of arc and occur at intervals of 1 to 2 sec. In between these are smaller
swinging movements, and superimposed on both are very small vibratory movements.
THE OPTICAL CHARACTERISTICS OF THE EYE 14-29
^ The voluntary movements are said to be conjugate if in the same direction, and disjunc-
tive if in the opposite direction, as when the eyes converge for a near object. The limits
within which the eyes can move without head movement determine the field of fixation.
Obviously, this will vary with anatomical features of the head, but it is illustrated typi-
cally in Fig. 5. The disjunctive movements are primarily concerned with convergence
movements within which binocular fusion can be maintained, and this is of importance in
ophthalmology since abnormalties in this function often lead to ocular discomfort. The
"far point" of convergence, which may be behind the head (a divergence of the eyes), can
best be measured by ophthalmic prisms, while the "near point" can be measured by
bringing a small object nearer and
nearer to the nose until doubling
occurs. Abnormalities in conver-
gence are frequently associated
with refractive errors but may have
more deep-seated innervational
origins. If one eye is covered
while the other fixates a given
point, the covered eye may deviate
from the direction of the point.
This deviation, when binocular
vision is prevented, is called hetero-
phoria. If the eye deviates out-
ward, inward, upward, or twists
about the fixation axis, the phorias
are said to be exophoria, esophoria,
hyperphoria, and cyclophoria re-
spectively. Almost everyone ex-
hibits at least a small phoria for
certain visual distances, and in
fact an exophoria of about 2 to 3
degrees for near objects would be
considered normal. Phorias fre-
quently are indications that sus-
tained efforts are being made to
maintain proper convergence of
the eyes in binocular vision.
Left Eye
SigHtEye
FIG. 5. An Illustration of Typical Monocular and Binocular
Fields of Fixation (from Asher, Arch. f. Opkthal.)
In reading or similar visual tasks, the eyes make a series of short interrupted movements
called saccadic movements. Even between two points, the movements do not occur
exactly but may arrive by a series of small successive approximations, one eye usually
leading. Eye movements are generally quicker in the horizontal than in the vertical
directions, and lateral movements are faster than convergence movements. Convergence
movements are more rapid than divergence movements. The speed of movement varies
with the excursion, attention, and other conditions, but on the average is between 100
and 200 degrees per second.
8. THE OPTICAL CHARACTERISTICS OF THE EYE
ABERRATIONS. In addition to the usual aberrations, the image on the retina of
the eye suffers also from irregular defects due to non-homogeneities in structure and the
lack of symmetry in the optical media. The axis of the crystalline lens is tipped and de-
centered with respect to that of the cornea. The visual axis, which is determined by
the fovea as well as the pupil, is usually decentered with respect to both the axes of the
cornea and the lens. The spherical aberration is asymmetrical From tbe central zone
of the pupil to the outside zones the eye tends to be myopic, increasing at first rapidly,
then reaching a maximum at 1 mm, beyond which the myopia decreases slowly, Tbe
problem of the spherical aberration of the eye is a complex one, and there are not yet
enough data to understand it satisfactorily. The chromatic aberration of the eye from
the C (656 mji) to the F (487 m/*) lines of the hydrogen spectrum amounts to about 0.7
diopter. The red rays are focused to a point beyond the retina; blue rays, to a point ante-
rior to the retina. The eye is said to be hyperopic to red, myopic to blue light. The
change in chromatic foci for equal changes in wavelength is much less toward the red but
increases markedly toward the blue. No entirely satisfactory explanation has been given
as to why chromatic halos about images of point light sources are not seen by tbe eye. For
emmetropes (individuals with no refractive error) the eye focuses approximately for the
D (580 mp) or yellow line of hydrogen.
14-30 OPTICS
Astigmatism at oblique incidence is a larger aberration. The primary (tangential)
astigmatic field differs only slightly from the surface of the retina out to 20 degrees, while
the secondary field rapidly increases in the myopic sense to nearly 11/4 diopters at a
peripheral angle of 20 degrees. There is very little coma in the eye, and the curvature of
the field approximates the curvature of the retina itself. The retinal image is believed to
have a slight barrel distortion, though this is difficult to determine because of the subjec-
tive asymmetries of the retinas.
These aberrations in themselves, together with diffraction phenomena, would tend to
reduce greatly the resolving power of the eye. However, as Gullstrand has pointed out,
these aberrations together produce a complex caustic surface in the cone of light converg-
ing toward the retina, so that actually the area of maximum light concentration in the
image may be small. This makes possible a resolving power whose limit is determined
only by the diameter of the receptor nerve endings.
REFRACTIVE ERRORS. The eye can be defective as the result of anomalies in the
refractive media or in the length of the eyeball, when it is said to be ametropic. The result
is blurred retinal imagery, with the attendant loss in sharpness of vision. Regular ame-
tropia is of two types — spherical and astigmatic. The first results from symmetrical
abnormalities of the refractive media, or from an increased or decreased length of the eye-
ball. Astigmatic errors result only from non-sphericity of the surfaces of the cornea
and/or of the crystalline lens. When the image focuses inside the position of the retina,
the eye will be nearsighted (myopic), because only when the objects are brought to the
eye will the images move back to the retina and appear sharply defined. In the reverse
case, when the point of focus is behind the retina, the eye is said to be farsighted (hyper-
opic), because nearer objects are the more blurred. Nearsightedness can be corrected
with a minus (diverging) ophthalmic lens of proper power before the eye; farsightedness
with a positive (converging) lens. When astigmatism is present, the light, after entering
the eye, focuses not as a point but as two lines separated in space and at right angles to
each other. Images of lines in space which are parallel to that focal line nearest the retina
will be seen more distinctly than those lines at right angles. For astigmatism, the corrective
ophthalmic lens before the eye must have one toric surface. Astigmatism may (and usually
does) occur in combination with spherical refractive errors.
Usually, when a refractive error is corrected by an ophthalmic lens, the magnification
of the retinal image cannot be predicted. A spherical refractive error due to an elongation
(or shortening) of the eyeball, when corrected by a lens, results in practically no magnifica-
tion (or diminution) of tbe retinal images. If the refractive error is due to abnormalities
in the refractive media, then a magnification (if the correcting lens is for farsightedness) or
a diminution (if the correcting lens is for nearsightedness) will occur. The degree of
magnification (or diminution) will be roughly 1 1/2 to 2 per cent per diopter power of the
correcting lens. Differences in the magnification of the images of the two eyes may result
in discomfort.
DEPTH OF FOCUS. As in any optical instrument, the image falling upon the retina
of the eye can be slightly blurred, because of the eye's being out of focus, without an appre-
ciable loss of perceived definition of the image. Thus, with the eye accommodated (fo-
cused) for a given distance, objects somewhat nearer and farther than this distance will
appear clear. The distance between the two limits of visual distance within which the
images on the retina appear not to suffer loss of definition is called the depth of focus.
This fact arises, in part, because the maximum light concentration is in the center of the
blur circle. Only when the intensity of this central portion is reduced as the blur circle
is broadened will there be a loss in definition. The spherical and other aberrations of the
eye are such that the depth of focus is greater than might be anticipated from ordinary
theoretical expectations. Owing to the constriction of the pupil with accommodation and
convergence, the depth of focus increases with the nearness of the fixation object. For
distance vision the depth of focus, measured as the difference of the reciprocals of the
nearer and farther limiting distances (in meters) for clear vision, is about 0.3 diopter,
which increases to about 0.7 diopter for a visual distance of 20 cm. With the eyes relaxed
for distant vision, and taking into account that the conjugate point to the retina is usually
not at infinity, one could expect all objects beyond 12 ft to be clearly defined. With
the eyes accommodated for the reading distance of 16 in. from the eyes, all objects from
about 14 1/2 to 17 !/2 in. will appear clearly defined.
9. THE LIGHT SENSE
THRESHOLD OF LIGHT VISIBILITY. It must be clear that all determinations of
visual thresholds, involve problems in psy chometrics (Guilf ord) . A given weak stimulus
THE LIGHT SENSE
14-31
may not always result in a definite response, and a still weaker stimulus will be responded
to even less often. One determines, then, the percentage of responses for a number of
exposures to the same stimulus strength. The stimulus strength is then varied in fixed
steps. What percentage of responses corresponds to the threshold is a matter of defini-
tion and varies with the experimenter. It is well to know this in trying to understand
and compare threshold data.
As a device for detecting radiant energy, the eye is exceedingly sensitive, though its
response is confined to a narrow region of the spectrum, from about 360 mp to 75O m/i.
The threshold of perception of light varies, of course, with the wavelength of the light, the
size of the stimulus, and the length of exposure to the stimulus. It is also different for
the cone and rod systems of the retina. Under optimum conditions, and taking the
threshold as the 60 per cent response to exposures, Hecht found that with different ob-
servers the threshold varied between 2.2 and 5.7 X 1CT18 erg measured at the cornea,
which amounts to about 58 to 148 quanta of light energy-. In this experiment a test light
was used, which subtended a visual angle of 10 minutes
stimulus of wavelength 510
of arc, and which was exposed
as a flash of 0.001-sec duration.
The test light was arranged to
stimulate rod vision 20 degrees
temporally from the fovea, and
the subject was, of course,
completely dark adapted.
The relative thresholds of
visibility for complete dark
adaptation of the rods and
cones of the fovea for different
wavelengths are illustrated in
Fig. 6 (Wald). Here the spec-
tral sensitivities (reciprocal of
the 'threshold stimulus
strength) are plotted. The
stimulus was a circular field
subtending a visual angle of 1
degree, and this was exposed
for 1/25 sec. For the r»d vision
a point 8 degrees above the
fovea was used. It is clear
from the figure that the rods
at an angle of 8 degrees into
the periphery of the retina are
2.5 times more sensitive than
the cones at the fovea. The maximum sensitivity (lowest threshold) for the cones occurs
at 562 mju whereas that for the rods occurs at about 505 m./*. The displacement of the
maxima toward the blue end of the spectrum from cone to rod vision is known as tiie
Purkinje phenomenon. The fact that at the red end of the spectrum the rods and coaes
have essentially the same threshold sensitivities is also of special importance.
The exact relationship between the area of the light stimulus and its intensity just at
the threshold of visibility is not entirely known. For the fovea, with areas less tbaa 10
minutes of arc, and for the periphery, for areas between 2 and 7 degrees, the product ol
the area and intensity is approximately a constant. This fact is known as Rieco's law for
the fovea and Piper's law for the periphery. These laws are wholly inadequate for wider
ranges of area, and, in general, for larger areas the product of area and intensity appears
to be a decreasing function of area.
In a somewhat similar manner, with a constant area, the relationship between intensity
and the duration of the stimulus is not fully understood. For brief flashes of duration ol
less than 0.2 sec, and with grnnTO areas, the product of duration of the flash and the intensity
is approximately constant (Bloch's law). However, for longer durations this constancy
no longer holds, and finally the intensity alone becomes the determining criterion for
threshold perception. It has also been found that the stimulation of one part of toe retina
by a small light source depresses the sensitivity of other parts of t3be retina for simultar-
neous but not for succeeding stimuli.
SPECTRAL LTTMIlf OSITTES, The so-called visibility curves for day light (yhoto&c)
vision and twilight (scofopic) vision are obtained in brightness-matcMng experiments- A
small area illuminated by a narrow region of the daylight spectrum is presented adjacent
to a standard field of constant brightness and one to which the eye is adapted. The sub-
FIG. 6. Spectral Senativities of the Rods and Cones of the Eye,
Expressed Relative to the Maximum Sensitivity af the Fovea
(Wald, Science)
14-32
OPTICS
0.8
0.7
0.6
0.5
0.3
0.2
0,1
A Aubert
o Koenlg
• Brodhun
ABIancha.rd
-5 -4
—3 -2-1 0 1
Log LuminosIty-MIIIIIamberts
PIG. 7. Typical Data Showing the Differential Threshold of
Brightness Discrimination (from Hecht, J. Gen. PhysioL)
ject adjusts the intensity of the colored light in the test area so that it is apparently equal
to the brilliance of the standard
field. The reciprocal of the inten-
sity of the transmitted spectral
colors for the match measures the
relative brightness values of the
visible spectrum. The data are ob-
tained when the brightness of the
standard field and the surround-
ings correspond to average day-
light intensities and again to twi-
light visual conditions. Figure 15,
p. 14-14, shows the curves which
are usually found but in which the
maxima are adjusted for the same
height. With luminosities above
about 0.01 lumen per sq ft, the
photopic or cone visibility curve,
which has a maximum at about
555 m/u, is found, while with lumi-
nosities below about 0.001 lumen
per sq ft, the scotopic or rod
visibility curve is found, with a
maximum at about 507 mju. For
brightness levels between 0.01 and
0.001 lumen per sq ft there is a
gradual shift of the position of the
curve, this being a transition from
cone to rod vision. The displace-
ment of the maximum is again the
Purkinje phenomenon. In very
low illuminations the eye responds less and less to the red while still responding to the
blue. No PurMnje displace-
ment is found for foveal vision
alone.
DIFFERENTIAL SENSI-
TIVITY. The smallest differ-
ence in brightness that can
just be perceived (just-notice-
able difference) between two
areas is a measure of the
differential threshold of visi-
bility from which one arrives
at a value of the differential
sensitivity, or contrast sensi-
tivity. The differential thresh-
old varies greatly with the
illumination, the wavelength,
the size and separation of the
test areas, and the luminosity
of the surroundings. The
differential threshold is ex-
pressed as the ratio AJ/I,
where 1- is the luminosity of
the standard area and the
^adapting field, and AJ is the
difference in luminosity of the
test area and the standard
area for the just-noticeable
difference in brightness. The
contrast sensitivity is the
reciprocal of this quantity.
Typical differential threshold
Contcast Sensitivity • I/Al
>-»»-» »-* h-4 t
K»-fcmooow£o>
o oo oo oo o<
o
/
o
/
/
L
arge Illu
Surro
minated
nd .
/
t
/
0
1
r
/J
I
DJ
rk Surro
undv
/
^
^-
•
/
V
/:
Roc
Vision ,
Lftaa°t^
-b.
A
—5 -4 -3 -2 -1 0 12 3
Log Background LumlnosIty-Lumens/fT8
FIG. 8. The Contrast Sensitivity of the Eye, Showing Data of
Koenig, Blanchard, Holliday, and Stiles and Crawford (after
Moon, Scientific Bases of Illuminating Engineering)
results are shown in Fig. 7, showing data recomputed by Hecht. Because of the wide range
in luminosities necessary, the abscissas are plotted on a logarithmic scale. In the photopic
TEMPORAL ASPECTS OF PERCEPTION
14-33
part of the curve the fraction AJ/7 is nearly constant, and only in this region can the
differential threshold of the eye be said to illustrate Weber's law. For very high luminosi-
ties a slightly decreased sensitivity may be found, but this can be attributed to uncon-
trolled illumination of the more peripheral surroundings of the test areas. That part of
the curve below 0.013 millilambert results from rod vision only, and a somewhat abrupt
change near that point is suggested by the data. It is sometimes more instructive to plot
the differential threshold data as the contrast sensitivity <//AZ), as shown in Fig. 8.
If smaller test and standard areas are used, the sensitivity is less, that is, the curve lies
higher on the AJ/7 axis of the differential threshold graph. Also it is found that, if the
luminosity of the surroundings outside of the test and standard areas is kept constant,
and then that of the standard area is varied, the differential threshold is increased (sensi-
tivity decreased), and the entire curve lies above the curve shown in Fig. 7. The luminos-
ity of the surroundings of the test field is an important factor in the contrast sensitivity
of the eye.
ADAPTATION. When one goes from a brightly illuminated room to one that is only
dimly illuminated, several minutes must elapse before details in the room can be discerned.
Likewise in going from the dark room into sunlight there are a few moments of blinding
glare. In either case, the eyes become adjusted to the prevailing brightness of the vitual
field in a few minutes. The retinal process by which this occurs, as well as the firm! sta-
tionary state, is called adaptation.
By the process of adaptation the
sensitivity of the eye to contrast
differences is automatically
changed to meet changing lumi-
nosities of the surroundings. In
light adaptation (photopic vision)
the visual sensitivity of the eye de-
creases; in dark adaptation (sco- J;
topic vision) it increases. In this
adaptation the eye adapts itself to
changes of illumination of several
thousand times.
Light and dark adaptations are
opposing processes and are differ-
ent for the cone and rod systems
of the retina. To a small extent
the pupil aids in the adaptation
processes. A typical curve show-
ing the progress of dark adaptation of the eye as a whole is shown in Fig. 9. The ordinates
indicate the luminosity of the test object at the threshold of visibility at any gi\~en mo-
ment in the progress of the dark adaptation. The upper curve results from the activity
of the retinal cones; the remaining part of the curve results from the rods. The data show
that foveal (cone) dark adaptation is nearly complete in 2 to 10 min. For the rods the
eye is essentially dark adapted in 40 min, though the sensitivity can still be shown to in-
crease slightly for longer periods of time in total darkness. Anomalies in dark adaptation
may be due to vitamin A deficiency.
The progress of dark adaptation varies somewhat with the siae of the test object and
especially with the intensity of the illumination in the previous light adaptation. There
is evidence also that the rate of dark adaptation can be increased and the dark adaptation
maintained when the observer wears dark red glasses, adequately shielded, in ordinary
illuminations (Rowland and Sloan).
The rate of light adaptation is very much more rapid than dark adaptation. Though
dependent upon the intensity of the adapting light, the sensitivity drops to a fraction of
its initial value within the first few seconds, and the light adaptation is nearly complete
in 1 min.
10. TEMPORAL ASPECTS OF PERCEPTION
PERSISTENCY OF VISION. From the instant the retina is stimulated to the moment
the first sensation occurs, a brief interval of time has elapsed. This interval, called the
latent period, which, in a sense, is a visual reaction time, depends upon the nature and
strength of the light stimulus and upon the adaptation of the retina. Under ordinary
light conditions, the latent period is roughly between 0.06 and 0.2 sec. As the intensity
of the stimulus is increased, however, the latent period decreases to a minimum (0.065 to
0.130 sec), beyond which further increases in intensity will not shorten the latent period.
1
-2
£
1-3
!«
i
-5
-6
I
*
!
SJ
x^Y^-
L
G
0
.W. 16 D
White Us
Eye as a
Red Cms
Fovea or
128
ht with
whole
\
*
s with
*y
\
V
^>o>a^
i-A Q
j-H r-j n n_
yp n_
10
15 2O 25
Ttoe to Dark-MSnetes
30
FIG. 9. The Dark-adaptation Curve of the Eye as a Whole
and of Lhe Fovea Showing the Behavior of the Cone and Rod
Svstems (Hecht, J. Gen. Pkysiol.)
14-34
OPTICS
Above the minimum, this interval varies approximately inversely as the logarithm of the
intensity. In dark adaptation, the latent period, for threshold conditions, may be 0.5 to
1 sec, depending upon conditions. The latent period is generally shorter in the peripheral
parts of the retina than at the fovea, and shorter for blue light than for red.
With a flash stimulus, the sensation persists for some time after the stimulus has ended.
The magnitude of the light sensation and its duration vary with the adaptation level of
the eye, that is, the luminosity of the
8 1 1 1 j \ 1 1 1 background upon which the stimulus
is seen and the strength of the stimu-
lus. Typical curves are shown in
Fig. 10. The duration of the im-
pressions from stimuli of equal
brightness is longer for the fovea
than for the peripheral parts of the
retina and is generally increased as
the eye is more dark adapted. An
increased intensity of the stimulus
results in a decreased duration time.
For colored light the persistence of
the sensation varies inversely to the
apparent luminosities of the visibil-
ity curves and hence is shortest for
yellow, longest for blue, and inter-
mediate for red.
After the first sensation has faded
away, several after-images may again
appear at intervals depending upon
the luminosity of the surroundings
and the intensity of the stimulus.
If the after-image corresponds to the
original impression as regards con-
trast and color it is called positive;
S?G* I?' ffi^teatiOT of the Apparent Brightness and the jf the Hght-to-dark relationships are
Duration of the Light Sensation Following a Flash Stun- f , , , , i
ulus (Data of Broca and Sulzer, from Luckiesh and Moss, reversed and the colors are comple-
Stience of Seeing) mentary to the original impression
it is called negative. Considerable
practice is sometimes necessary to see these images, for conditions of fatigue, adaptation,
and inhibition may greatly affect their appearance. The typical sequence of after-images
is illustrated in Fig. 11, where the ordinate represents the relative brightness of the after-
images, positive above and negative below the abscissa.
0.2
Time In Seconds
VIII (6)
667
Time In Seconds
10
11
FIG. 11. Diagram of the Sequence of After-effects Folio-wing a Flash Stimulus in the Light-adapted Eye
(after Tschermak-Bethe, Handb. normal u. path. Physiol., 12/1, II)
PERIODIC STIMTJLI AND FLICKER. Periodic light stimuli may be perceived as
discrete flashes, but if made sufliciently rapid, so that the persistent sensation from one
stimulation curve overlaps the rise of the primary sensation from the succeeding stimula-
tion, the sensation will be the same as that for a continuous illumination.
The brilliance of fused periodic stimuli which have different intensities is the same as
the average intensity (TaJbot's law), that is, the integral of the photometric luminosity
of the periodic stimuli divided by tune. This law holds accurately except for extremes of
high and low intensities. That frequency at which periodic stimuli are first perceived as
a steady illumination (fused) is known as the critical flicker frequency, which may be
abbreviated to e.f .f. The critical flicker frequency varies with the illumination, the part
COLOR
14-35
of retina being stimulated, the area of the flickering field, the ratio of the light-to-dark
intervals of the flashes, the retinal adaptation, the wavelength of the light, and the pres-
ence of other steady light stimuli also falling upon the retina. So reliable is the c.fX
under controlled conditions that it is sometimes used to measure luminosities and adapta-
tion levels.
The manner in which the c.f .f . for small test fields illuminated with white light varies
with illumination and for different parts of the retina is shown in Fig. 12. In the rod-free
area at the fovea, the c.f.f. varies proportionately with the logarithm of the illumination
(Ferry-Porter law), except at the extremes of the iUuminatioa. The maximum critical
frequency is about 53 cycles per second. The c.f.f. decreases for flicker stimuli on the
peripheral parts of the retina. If the area of the flickering field is large, however, the
60
W
o
20°
-5
—3
-1
FIG. 12. The Relationship between the Critical Flicker Frequency and the Illumination, for Different
Parts of the Retina (Hecht, J. Gen. P&yswjJ.)
critical frequency may be found higher in the periphery, which indicates a spatial summa-
tion of the retina in the periphery. The curves generally appear to be in two parts, a
division which is attributed to the rod and cone behavior. The c.f.f. for various colored
stimuli is substantially the same as for white light if their apparent luminosity is the same
as that of the white light and the intensity is above the cone threshold.
In the curves shown in Fig. 12, the duration of the light phase was equal to that of the
dark. Where the dark phase is longer, generally higher critical frequencies are found, and
when shorter, lower critical frequencies are necessary, especially in the ordinary ranges, of
illuminations. Only at high intensities of the light stimuli will this generalization be in-
valid. Rapid eye movements or rapidly moving periodic stimuli enhance the appearance
of flicker, and under these conditions higher frequencies are necessary. A steady illumina-
tion of one part of the retina changes the c.f.f. of a periodic stimulus in another part if
the separation of the two stimuli is not too great. In general the c.f.f. increases as the
brightness of the steady stimulus is increased, until a maximum is reached, beyond which
it then decreases.
Hartley found that for periodic stimuli below the c,f.f., and at about 8-10 flashes per
second, there is a marked enhancement of the apparent brightness of the stimuli.
11. COLOR
A clear differentiation must be made between the color s*w»«Ius and the color sensation.
The color sensation and all the associated phenomena are purely psychological (experien-
tial). The stimuli measured in terms of energy and wavelength are physical. The color
problem is fundamentally the finding of the relationships that exist between the color
14-36
OPTICS
sensation and the physical stimuli. Moreover, relationships found for color mixtures
from spectral light will not necessarily be true when colored pigments are mixed. This
fact has led to much confusion and controversy. The spectral luminosities reflected from
pigments, however, are subject to the same laws as those from spectral light.
Colors are ordinarily seen as properties of objects and hence are usually associated with
the objects themselves. There are, therefore, many psychological constancy phenomena
in which objects tend to retain their color and brightness when seen in varying conditions
of light and shade. Photographic scenes in color projected in an otherwise darkened room
tend to retain normal color relationships in spite of actual wide deviations. Under other
conditions where these reproductions are viewed against backgrounds of stable color and
contrast relationships, these deviations are more readily apparent. To study correlations
between the quality of color experience and the physical composition of light, the test
fields must be dissociated from known objects having spatial values. These psychological
facts are important in dealing with color problems.
A given color sensation is said to have three dimensions: hue, saturation, and brilliance.
Hue is associated with the dominant wavelength of the light stimulus. Saturation indi-
cates the amount or degree of the hue present (deep-red as against pale-red) and repre-
sents the ratio of the luminosity of the pure spectral light to that of the white light present.
Brilliance (apparent brightness, apparent luminosity) indicates the total intensity (energy)
of the colored light stimulus. Frequently, hue and saturation are considered together
under the term chromaticity,
SATURATION OF THE SPECTRAL COLORS. All spectral colors do not appear
equally saturated, that is, some have a greater sensation of white than others. The ratio
of the luminosity of the least perceptible spectral color to the luminosity of a background
field defines the least-perceptible colorimetric purity for that color. Two halves of a test
field are equally illuminated with white light. To one half a spectral color is added, and,
in order that the brightness of the two fields shall be the same, the luminosity of the white
light of that field is decreased as the spectral color is added. The intensity of this spectral
color is then increased until the two halves of the field just appear different in color. From
the luminosity of the added spectral colors the colorimetric purity of the spectrum can be
found. Figure 13 illustrates data obtained in this manner. It is clear that a great deal
O.ioo
0.050
0.001
400
500
Wavelength-m^t
600
700
FIG. 13. The Least-perceptible Colorimetric Purity of the Visible Spectrum (Data of Priest and Brick-
wedde, after Hecht, J. Gen. Physiol.}
more of yellow than red or blue is required to produce a least-perceptible color, and yellow
is therefore considered a less saturated color than red or blue.
HTTE DISCRIMINATION THRESHOLD. The change in wavelength corresponding
to a just-noticeable difference in color varies over the spectrum and also somewhat with
COLOR
14-37
the individual. In general, however, the data are similar, and the resultant curves show
three maxima and three minima. In Fig. 14 are illustrated representative data for an
individual with normal color vision. The dis-
crimination is poorest at the ends of the spec-
trum, especially in the red.
COLOR SPECIFICATION. The color
stimulus (as distinct from the color sensation)
of any color field can be specified quantita-
tively by the luminosity of the radiation given
off for each part of the spectrum. This can
usually be measured by a speetroradiometer
or a spectrophotometer. Under any condi-
tion, the objective color from a given surface
can then be specified by a spectrophotometric
curve obtained from those measurements.
The eye itself cannot analyze the radiation
from a color stimulus as can the spectro-
photometer, for it responds in a complex
manner dependent not only upon the visual
processes and their reaction to light stimuli
but also upon certain psychological factors.
There are, therefore, many different objective
color stimuli, as specified by spectrophoto-
metric curves, which will result in the same
color sensation. It is possible, however, to
transform the data from the spectrophoto-
4OO 440 4SO 52O 56O 600 640 680
FIG. 14. The Least-pereeptibk IKfferasee in
Color for the Viable Spectrum (Data of Jones,
J. Optical See. Am.)
metric measurements by means of standard data from color-matching experiments, so that
equal color sensations can be specified by three quantities derived from the objective
stimulus.
The I.C.I. (International Commission on Hlumination) system is that most used for
accurate color specification. It is
based upon the theory that the
chromaticity (hue and saturation)
of any color stimulus can be speci-
fied by three Quantities, which rep-
resent the proportions of three
selected primary light distributions
that are necessary to match the
color sensation evoked bj a given
stimulus. The amounts (luminosi-
ties) of each of three selected pri-
mary color sources that must be
added together in order to match
a given spectral color are deter-
mined by these color-matching
experiments. These amounts are
called the tristimulus vahies of the
three primaries for that color.
Three standard spectral distribu-
tions of equal energy, whose tri-
stimulus values are x = /*(X),
$ » /S(X), and s = /*(X) (X being
wavelength), are especially se-
lected, with dominant wavelengths
in the redT green, and blue respec-
tively. Of. Fig. 15. These pri-
mary distributions are obtained by
400 440 480
640 680 720
520 560 600
Wavelength, rap
FIG. 15. Tristimulus Values for the Various Spectral
Colors. The values x, y, z are the amounts of _ the three
I.C.I, primaries required to match in color a unit amount
of energy having the indicated wavelength. (Hardy, H<md-
book of Colarimetry.)
transformations from the experi-
mental data with real primaries;
they are specially selected to avoid
negative tristimulus values and to
meet other requirements for a convenient system. The y spectral distribution function
has been made to correspond to the photopic visibility curve. Any homogeneous spectral
radiation can be specified by the tristimulus values read directly from the curves or special
tables (Hardy). For a spectral radiation objectively specified by a spectrophotometric
14-38
OPTICS
curve, the tristimulus values are found by summing up the products of the energy E\ for
all wavelengths by the corresponding tristimulus values from the standard primaries from
the tables, viz.,
Through the choice of primary standard distributions the second integral gives directly
the relative luminosity (brightness) of the color stimulus on a black (zero) to pure white
(100) scale. In practice, the tristimulus values for any spectrophotometric curve are
computed by averaging the products of xE\ (and yE\ and zJ?x) for equally (spaced wave-
lengths.
^ The values of a;', y', and zr do not necessarily measure the color sensation, but they do
state the conditions under which different spectral stimuli will result in the same color
sensation. It must be borne in mind that this sensation may vary slightly between indi-
viduals and even with other factors, such as size of field and conditions of the surround-
ing fields.
THE CHROMATICITY DIAGRAM. A convenient graphical representation of the
chromaticity of any spectral stimulus is made by plotting the trichromatic coefficients
which are defined by the ratios
x' , y'
* = x> + y> + *> ^ *" * + y> + *
and the third would be related to the other two by x + y + z — 1. The result is the
standard chromaticity diagram in which colors of equal luminosity are represented in
terms of dominant color and
°-9 ' ' saturation. See Fig. 16. Color
matches are known to be
stable through wide limits of
luminosity; hencejthis repre-
sentation is valid.
The visible spectrum ar-
ranges itself in a horseshoelike
curve beginning with red
(700 mju) and passing counter-
clockwise through orange,
yellow, green, blue to a deep
purplish blue (400 m/z). The
straight line joining the ends
of the spectrum contains the
purples. Clearly, this line is
not part of the spectrum.
White light is represented by "
various points on a curve
near the center of the dia-
gram, its exact position de-
pending upon the tempera-
ture of the source. The
luminant recommended by
the International Commission
on Illumination is shown on
the diagram at C. Any given
color stimulus will also be rep-
resented by a point within
this curve. Figure 17 shows
the approximate color names
0.6
0.7
0.8
FIG. 16. The Chromaticity Diagram, Showing the Geometrical
Arrangement of the Spectral Colors and the Locus of White Lights
(after Hardy, Handbook of Col&rimetry)
for the different portions of the diagram. The dominant wavelength of any stimulus'will be
given by the place where a straight line drawn through C and the point intersects the nearest
part of the spectral curve. The complementary wavelength will be the intersection point
on the spectral curve diametrically opposite. The saturation or excitation purity of a
given color can be determined from the ratio of the distances of the point from C, and
from the dominant wavelength on the spectrum curve. The resultant color of a mixture
of any two colors represented by two points on the I.C.I, diagram will be represented
somewhere on the straight line drawn between the two points. The advantage of this
representation is its direct quantitative application to spectrophotometric data. Its
disadvantage, however, lies in its graphical distortion of color differences.
THE SPACE SENSE
14-39
OTHER SYSTEMS. The Ostwald and Munsell systems consist of orderly arrange-
ments of colors based upon their visual relationships, and not dependent upon the mixture
of pigments or upon the physical measurements of the light, and independent of the illu-
mination. Both these systems are illustrated in carefully prepared charts with orderly
arrays of colored patches, which vary in hue, saturation, and value according to the con-
cept of the author.
COLOR TOLERANCE. Nearly as important to color specification is the necessity of
knowing color tolerances. The most thorough study, to date, is that of MacAdam in
which the color tolerances in
changes in hue and in saturation °'9
were determined.
COLOR ADAPTATION. If the
eyes are subjected to a large field
of a spectral color for a period of
time, the perception of hue of other
colors becomes modified and dis-
torted. This may be in the nature
of an adaptation. Two electric
lamps, one white and one colored,
say red, are set in front of a large
white screen several feet apart.
Then an object is placed nearer
the screen in between the lamps,
so that two shadows, one from the
white and one from the red lamp,
are cast upon the screen. Upon
continued observation it will be
found that the shadow cast from
the red lamp will appear green,
complementary to the red color,
while the shadow from the white
light will appear red. In the gen-
eral perception of colored objects
in fields of familiar detail, the color
relationships tend to remain the
same, in spite of rather wide vari-
ations of illumination intensities
and even color. If the visual fields are isolated and confined, however, to small areas, apart
from the larger field, this color-constancy phenomenon tends to disappear.
0,1
0.8
FIG. 17. Approximate Color Names for Various Parts of the
ChromaticityfDiagT&ra (Kelley, J. Opticci Soc~ Am.)
12. THE SPACE SENSE
It is necessary to distinguish clearly between objective space, filled with real obje<yts,
and visual space, filled with visual objects. It is somewhat meaningless to ask whether the
position of visual objects is identical to that of the real objects. It is only necessary that
the relationships between visual space and objective space be ssifikaently stable so that
the organism can effectively operate within real space. Tbe visual perception of space is
essentially egocentric in that objects are localized with respect to the body. The final
perception of space arises through a complex integration of (1) the visual clues inherent in
the pattern of the dioptric images that fall on the retinas, (2) the simultaneous impres-
sions from the other senses, (3) experiential factors that have been associated with visual,
auditory, and tactile stimuli, and (4) the immediate attention of the individual. It is
convenient to regard space perception in terms of (1) the discrimination of direetiom (ego-
centric and bidimensional), and (2) the discrimination of depth, that is* the third dimen-
sion.
DIRECTION LOCALIZATION. By virtue of the discrete make-up of the refea (tfee
retinal mosaic), the various parts of the dioptric images on the retina can be differentiated
through some type of "local signs" associated with the retinal elements, which, in this
case, is a subjective visual direction. Resolving power and visual amity are measures of
the keenness with which this differentiation can be made. The fovea is the primary
point of reference, and the subjective direction of objects is described in terms of '^breadth"
(right or left) and "height" (above or below) the point of fixation which is imaged on t&e
fovea. The subjective visual directions then are relative to the fovea. By a reSex process
associated with the eye, head, and body movements, the change in the subjective direction
14-40 OPTICS
of the whole visual field that would occur with eye movements is counteracted, so that
objects tend to appear in the same "absolute'* direction in spite of the fact that the images
move across the retina.
Tbe precision of the relative subjective direction varies greatly with the character of
the visual field, and in many cases estimations actually are inaccurate. Probably the
highest precision is in the estimation of when lines are parallel or when they are straight,
and in the comparison of angles whose corresponding sides are parallel. In the estimation
of differences in length, a greater precision is found in the horizontal than in the vertical.
Vertical distances, moreover, look longer than equal horizontal distances. In the estima-
tion of lengths, accuracy varies with the lengths to be compared and their relative posi-
tions. When attempting to determine the center of line segments without eye move-
ments, the eye tends to overestimate the portion on its own side (Kundt partition phe-
nomenon), though frequently the reverse is found. Subdivided and nlled spaces look
longer than unfilled spaces. Acute angles are generally overestimated and obtuse angles
are underestimated. Magnitudes are diminished in the presence of larger magnitudes
and magnified in the presence of small ones. Many of the well-known illusions are exam-
ples of these errors in the perception of direction.
VISUAL ACUITY AND RESOLVING POWER. The visual acuity of the eye is the
degree to which it is able to discriminate fine detail in the visual field, and this varies
considerably with the type of detail, the contrast, illumination, surrounding brightness,
adaptation level, etc. In a strict sense, resolving power is more definitive than visual
acuity; it is measured as the reciprocal of the smallest visual angle (usually in minutes of
arc) by which two objects can be seen separately. The theoretical limit of visual resolution
would be determined by the size of the diffraction circles on the retina and the dimensions
of the retinal elements. However, for pupils of normal and larger sizes the spherical and
chromatic aberrations, together with small irregular astigmatism that is usually present,
modify the nature of the light intensity distribution within the image, so that, with the
contrasts ordinarily encountered, the resolution is better than that based upon diffrac-
tion alone. For small pupils a marked decrease in acuity is found, probably resulting
from the increased size of the diffraction circles, but for pupils larger than 2 to 3 mm the
acuity remains nearly constant (Cobb). Faint stars whose angular separation is 1 to
1 Vs minutes of arc can usually be resolved. With small point light sources of low con-
trast with respect to the background, the minimum angle of resolution may be 100 seconds
with a mean error of 5 seconds of arc. With repeating patterns such as lattices, grids, or
checkerboard patterns the minimum angle of resolution varies between 50 and 75 seconds
of arc, under optimum conditions.
The eye is, of course, capable of much finer discrimination of detail than that which
would be obtained on the basis of resolving power alone. Experiments which indicate
this fine appreciation of detail involve least-perceptible differences in contours. These
differences have been expressed as the mean error of settings, or in the 50/50 point, in
correct judgments. Typical results are shown in the table below.
Mean Error,
Test seconds Authority
Widening of lower half of slit 10-12 Wulfing (1892)
Coincidence of vertical lines (the vernier) 8-12 Brian and Baker (1912)
Coincidence of vertical lines (the vernier) 13 Best (1900)
Coincidence of vertical lines (the vernier) . , . . , 3 Langland (1929)
Coincidence of vertical lines (the vernier) 0.6 Trench (1920)
Coincidence of vertical lines (the vernier) 2 Wright (1942)
Error in contact of white disks on dark background. . 15 Dale (1920)
Alignment of edges of two rectangles 10 Hering (1899)
Error of setting range finders 2-6 von Hof e (1920)
Stereoscopic displacement of images 5-7 Florian (1930)
In general, where such fine discrimination can be seen, the retinal images of the detail
(such as extended lines) involve the activity of a larger number of retinal elements. Except
for monochromatic yellow light, visual acuity is decidedly poorer under colored illumi-
nants than under white light. This is especially true of blue and only slightly less so under
red illuminations. Part of this latter decrease in acuity is undoubtedly related to the
chromatic aberration of the eye.
Visual acuity is usually measured by a test chart of letters of graded sizes, in spite of
certain obvious inherent faults. Visual acuity is considered normal when letters can be
identified the separation of adjacent parts of which subtend an angle at the eye of 1 minute
of arc. A line of letters, each of which subtends a 5-minute visual angle, is printed on a
chart in sequence for visual distances of 10, 15, 20, 25, 30, 40, 60, 100, and 200 ft. These
letters are usually arranged with the smallest at the bottom of the chart, and with a single
THE SPACE SENSE
14-41
large E at the top. The acuity tests are usually made at a visual distance of 20 ft, and
that line of letters which the subject can just read is then recorded relative to 20 ft. Thus
20/20 represents normal vision; 20/15 indicates that print which could ordinarily be read
at 15 ft can be read at 20 ft and therefore the acuity is better than normal; and 20/100
indicates that that type which should be legible at 100 ft can be read only at 20 ft and
therefore the acuity is much less than normal. Other test objects frequently used are
the Snellen hook, the Landolt broken ring, and checker-board patterns.
Because of the increased size of the photosensitive elements toward the peripheral parts
of the retina and the greater number of them associated with single conductor nerves,
together with the increased magnitude of the optical aberrations toward the periphery of
the eye, it is to be expected that the resolving power of the eye would fall off rapidly
toward the periphery. Figure IS shows this decrease in resolving power with the increase
70° 60° 50° 40° 30° £0° UD° 0° 10° 20° 30J 4O° 50° 60
Temporal
Fig. IS. The Decrease in Visual Acuity toward the Peripheral Parts of the Retina (Wertheim)
of the peripheral angle (data of Wertheim). A very rapid decrease in acuity occurs to
about 5 degrees, and from there the decrease is much slower. This loss of acuity is not the
same in all the meridians of the eye but is greater in the vertical meridian than in the
horizontal. Figure 19 shows the isopters of the retina, that is, the curves of equal visual
acuity (data of Wertheim).
90°f 80°
70° 80C
90*
\
PIG. 19. Isopters of Retina, or Curves of Equal Visual Acuity, Showing that the Decrease in Acuity is
Greater in the Vertical Meridian than in the Horizontal (Wertheim)
14-42
OPTICS
There has been evidence that visual acuity is greater for distant vision than for near
vision. This phenomenon is believed to be dependent upon the type of test and the condi-
tions under which the test is made, especially for peripheral vision, because opposite results
have been reported.
IRRADIATION. Owing to the aberrations of the optical system of the eye, the images
of discrete points are not denned with sharp boundaries. Rather, the intensity of the
light in the image falls off in a bell-shaped curve. The perceived contour depends upon
the differential sensitivity of the eye, but the image always corresponds to an object larger
than the original. The position of the perceived contour will tend to be toward the less
intense end of the light distribution curve. Accordingly, bright objects seen against a
dark background appear larger than dark objects of equal size against a bright background.
This phenomenon, called irradiation, depends upon the relative luminosity of the adjacent
surfaces and varies with individuals because of differences in ocular aberrations. Objects
of large angular size are increased proportionately only to a small extent, and their size
can be said to remain constant. For small objects, however, the irradiation increases with
decrease in angular size. On the other hand, the separation of small black lines against
a bright background may actually appear larger than it is. This so-called negative "irra-
diation" is explained, however, by the influence of the mechanism of simultaneous contrast,
whereby the apparent brightness (or color) of an area is influenced (enhanced) by adjacent
areas of different brightness (or color) .
VISUAL ACUITY AND ILLUMINATION. The visual acuity of the fovea of the eye
increases markedly with an increase in the luminosity of the field, but that of the periph-
eral retina changes scarcely at all. In
general, then, studies on visual acuity
and illumination pertain to foveal
vision. The data of Konig illustrated
in Fig. 20 (as recomputed by Hecht)
are among the most complete on this
phenomenon. They were obtained
with a black test object upon a white
background and are therefore of maxi-
mum contrast. For illuminations
from 0.013 to 10 lumens per sq ft the
visual acuity is approximately propor-
tional to the logarithm of the lumi-
nosity. The visual acuity obtained at
lower illuminations decreases rapidly
in the neighborhood of 0.001 lumen
1.8
1.6
1.4
1*2
fl.O
4?
§0.8
0.6
0.4
0.2
-5 -4 -3
2-1 0 1
Log I-mnniamberts
per sq ft, where scotopic vision begins.
From here, for lower illuminations,
only rod vision is involved and the
change in visual acuity is small. Al-
though Konig's data show a maximum
for illuminations greater than 100
FIG. 20. The Relation between Visual Acuity of the Iumens Per sq ft, and thereafter a con-
Fovea and Illumination (Data of Koenig revised by stant visual acuity, more recent data
Hecht, J". Gen. Physiol.) have indicated that this maximum is
,, - ,, , , , , due to the fact that the brightness of
tne neld surrounding the background of the test object was low compared to that of the test
object itself. In experiments where the brightness of the surrounding field is the same as
that of the background for the test object, a maximum is not found and the visual acuity
continues to increase at only a slightly lower rate with a continued increase of illumina-
tion. The visual acuity is lower for colored light than for white of the same brightness,
being poorer in the order green, red, blue. In general, visual acuity is also reduced under
conditions of glare.
When detail is exposed for short intervals of time (less than about 1 sec), and the
luminosity of the background remains constant, the visual acuity varies roughly with
the logarithm of the time of exposure. Below exposure times of about 0.01 to 0.03 sec,
depending upon the illumination, the product of time and illumination is constant for the
same visual acuity.
In Konig> data the contrast, defined as the ratio of the difference in luminosity of the
background and the test object to the luminosity of the background, was very high. It
has been shown that with lower contrasts the visual acuity is also lower. Figure 21 illus-
trate data from Cobb and Moss on the relationship between contrast and visual acuity.
-No data are available for bright detail against a darker background.
THE SPACE SENSE
14-43
MINIMUM VISIBLE. Similar to the problem of visual resolution is that of the mini-
mum visible. What is the angular size of the smallest detail that can be perceived? As
in resolving power, this depends upon an intensity
discrimination within the image on the retina and
hence varies with the nature of the dioptric image,
the contrast sensitivity of the eye, the size and
form of the detail, exposure time, etc. Lines are
more readily seen than dots, and repeating patterns
of dots, lines, etc., are perceived even more readily.
Small voluntary and involuntary eye movements
also aid in the discrimination of fine detail. Under
general illumination a line against a bright back-
ground can be seen when its width subtends a visual
angle of 3 to 4 seconds of arc. Hecht and Mints
found that with a similar test object the angular
width of a wire that could just be seen varied from
10 minutes to 0.5 second over the complete range
of illuminations. The rninimum value 0.5 second
represents a discrimination of about 1 to 2 per cent
difference in light intensity in the image on the
retina. When a narrow illuminated slit that is ex-
posed for short durations is just visible, it is found
that (visual angle) X (duration of exposure) X
(adapting luminosity of background) is approxi-
mately a constant for flashes of 0.004 to 0.189 sec
of duration (Niven and Brown).
As indicated above it is now believed that the
rate at which contrast sensitivity and visual
100
21. Relationship between Minimum
Angle of Resolution, Luminosity of Back-
ground, and the Contrast of the Test Ob-
ject Relative to its Background (Cobb and
Moss, J. Frankiin Im&itvle)
acuity in the absence of glare increase with luminosity of background is not appreciably
diminished with the very high luminosities (cf. Figs. 8 and 20). In other words, there
is no optimum luminosity. The question arises then as to what the general illumination
should be for adequate vision. Although this question cannot be answered specifically
B
Relative Visual Prof IcJancy- Par cent
to.bg) Co to to to <p q
^O OOO O 0 4* CO do 3
/
/
/
Contrast Sen
sitlvlU /
7 x
x'
/
/ /
X'
Minimum VI
1W9^
/ /"
al Acuity
/
^
/^
f
x*^
X
Ne:
rttlnd**,
Noon
,..-'^S
f,^
Ii
iteriorsx
>/ D.
jyjfett
Skyj
.
- - -~^
" \
/
r-^
^U /
&•* a 10 io2 ios 10* io6 ic
Luminosity of Backgrocrad-Lamens/Sq.Ffc.
Fia. 22. Relative Visual Proficiency for Contrast Sensitivity, the Minimum Visible, and Visual Acuity,
as a Function of Brightness of Background (after Moon and Spencer, J, Optical See. Am.)
it is of value to know the relative degree of visual efficiency for any given general
illumination. A scheme for indicating this has been suggested by Moon and Spencer. In
contrast sensitivity, the quantity Tc is denned as the ratio of the contrast sensitivity
14-44
OPTICS
(J/AI) for the given illumination (I) to the maximum contrast sensitivity that would be
obtained with uniform fields and very high daylight luminosities. It represents the rela-
tive proficiency of contrast discrimination at any given illumination. Similar ratios Tv and
Tc are defined for the minimum visible and for visual acuity. In Fig. 22 the theoretical
values of each of these three visual functions are shown as dependent upon the luminosity
of the background. For outdoor lighting the relative visual proficiency would range
between 70 and 95 per cent, and for interiors with artificial lighting it would probably be
less than 80 per cent.
PERCEPTION OF MOTION. The motion of objects in space is perceived as motion
relative to the observer or as relative motion between the objects themselves. Under
special circumstances the motion of objects seen with respect to each other and to the
observer may be equivocal, for example, the apparent motion of the moon observed through
moving clouds. In a field of large and small objects the larger objects are said to exhibit
more stability and are less liab.le to apparent motion, while small objects exhibit apparent
movement more readily and are said to be more mobile. Moreover, objects imaged on the
peripheral parts of the retina appear less mobile than those falling on the fovea.
Perception of motion rests upon a temporal reaction to stimuli falling successively on
neighboring points of the retina, but its appreciation appears only partially related to
resolving power. It is thought to be a visual sensation resulting from experience. For
objects whose visual angle of movement is small, motion is inferred from the apparent
positions after lapses of time, for example, a moving train seen at a great distance. The
true perception of motion, however, is a specific sensation, with both lower and upper
thresholds of discrimination. The impression of motion can also occur (within definitely
prescribed limits) from successive stimuli arising from separated stationary sources. This
is called apparent movement by psychologists.
The threshold of the perception of true motion relates to the least angular ^displacement
of an object that can be recognized in unit time. With comparison objects in the field of
view the lower threshold is 1-2 minutes of arc per second. Without comparison objects
this value must increase 10 to 20 times. The least angular movement that can be detected
between two fixed points is sometimes called the movement acuity; under ordinary cir-
cumstances, this is found to be 10 to 20 seconds of arc, when stationary comparison
objects are in the field of view. Without comparison objects this increases to more than
1 minute of arc. When the range of
70
| 60
*0
JJ50
A40
I
I2
5
J20
llO
Form Acuity-
Blind
Spot
Motion Acuity
the movement (the distance between
the beginning and end points) is fixed,
the shortest lapse of time in which
motion is seen has also been measured.
Under ordinary circumstances, for ex-
ample, the threshold for a 10~degree
range varies between 0.027 and 0.079
sec. The upper limit for the discern-
ment of motion, when the sensation
becomes a meaningless blur, is 1.4 to
3.5 degrees per Vioo sec. The move-
ment acuity decreases with increase in
illumination.
The threshold for the discrimination
of movement is least at the fovea and
increases rapidly out toward the periph-
ery of the retina, though it has been
thought that the increase is much less
than the decrease of visual acuity to-
ward the periphery. Figure 23 illus-
trates the data of Klein, which show,
however, that the acuity and motion
thresholds are essentially the same ex-
cept at the fovea. It appears that the discrimination of motion is greatest at the fovea,
but the appreciation of motion is most marked in the peripheral retina, to a degree be-
yond the actual resolving power. The discrimination of movement in the periphery jis
somewhat poorer above and below the fovea than to the right or left. There is a tendency
to overestimate the extent of motion in the periphery, and, furthermore, the subjective
direction of that motion is somewhat vague and uncertain. However, the sense of
movement is highly developed.
THE PHI-PHENOMENON. The impression or illusion of movement can occur in
certain situations without there being actual physical movement. The most important of
20 30 40 50
Peripheral Angle- Degrees
70
FIG. 23. The Thresholds for Form Acuity and Motion
Acuity for Same Test Objects. The motion acuity is
given in terms of the minimum distance required for
perception of motion. (Data of Klein, Arch. Psychol.)
THE SPACE SENSE 14-45
the apparent movements is known in its purest form as the p&i-phenomeiaa, whereby
apparent movement can occur, under certain conditions, when separated stationary points
are illuminated successively. Usually the illusion of movement can be distinguished from
real motion, however, and, as such, may be variously interpreted by different observers.
Only in the neighborhood of an angular succession of 20 degrees per second are tlie two
motions difficult to identify (de Silva). For the impression of motion there is a time rela-
tionship between the duration of the first stimuli, the separation of stimuli, the interval
between successive stimuli, and the brightness of background, the impression depending
also to a great extent upon the attitude of the observer. Under ordinary conditions, with
a dark background, it has been found that, for two point stimuli 1 cm apart, the duration
of each of which is 0.05 sec: (1) if the two stimuli are nearly instantaneous (0.03 sec) they
will appear simultaneous; (2) if the time interval is greater than 0.2 sec the points will
appear discrete and stationary; (3) for time intervals intermediate between these two
there will be an apparent movement of the first point to the second, with an optimum at
0.06 sec. Of two light points of different intensity the weaker tends to move toward the
brighter. Other examples of apparent movement are in the cinema, in neon signs, and in
stroboscopic instruments.
THE PERCEPTION OF DEPTH. In the perception of depth one must distinguish
between the perception of depth differences (how much one object appears in front of or
behind another) and the absolute localization by which the actual distance of objects
from the individual is estimated. Binocular vision, through the phenomenon of stereopsis,
provides the most accurate means of relative depth discrimination.
The absolute localization of objects in space results from a complex process that involves
both monocular and binocular perception. It has been usual to state that the perception
of depth by monocular vision is a conception of depth (distance) attained through expe-
rience with certain relationships (clues) that will exist between parts of the retinal images
of different objects in space. The more important of these visual clues are: (a) Overlay,
by which the images of near objects overlap and tend to hide those of the naore distant
objects, (b) Perspective, which depends upon the fact that objects of eo^ial size have
smaller retinal images when at a distance than when near by. linear perspective relates
to the apparent convergence of parallel lines that recede in the distance (railroad tracks,
etc.). Details within known objects are more readily seen when near than when distant.
Thus, the size of retinal image related to known size provides the clue for estimation of
distance, (c) Aerial perspective, through which the edges of objects at a distance are leas
clearly denned than those near by. Moreover, the more distant objects appear cooler
(bluer) in color on account of atmospheric haze. Near objects appear brighter with more
color saturation than those more distant, (d) Light arid $hadou\ which give clues as to
shapes and relative positions of objects, (e) Parallax, which results from head movements,
for the relative alignment of more distant objects changes less than that for near objects
with the same movement. This clue to depth perception is very strong, and the precision
of depth estimation through it is nearly as great as that of stereoscopic depth perception
(Tschermak) . (/) Height, whereby objects seen above others are also judged more distant.
(g) To a small extent accommodation and convergence, through a proprioceptive sens*
arising from the muscles of the eyes, may provide a due for gross differences in depth.
As is well known it is impossible to present a single bidimensional picture which will
have all the characteristics of the actual three-dimensional scene being portrayed. This
is especially true when the picture is being viewed binocularly. As the eyes move over a
painting, no change in accommodation or convergence is demanded and obviously no dis-
parity clues are present for stereoscopic space localisation of the details in the picture as
there would be in the actual scene. The perspective in a pictorial representation of any
scene, whether a photograph or a painting (except in certain art styles) , refers to a fixed
station point and in order to appear correct must be viewed from that point. A contact-
print photograph should, then, be viewed at that distance that approximates the focal
length of the camera that took the photograph. Viewed at other distances the perspective
is exaggerated and unnatural. The viewing distance of an enlarged photograph will be
equal to the product of the focal length of the camera and the magnification of the en-
largement. This larger viewing distance explains the more pleasing effect derived from
looking at enlarged photographs. It is desirable that pictures be viewed in such a way
that the observer feels himself a part of the scene. The screen or plane of the picture
itself should seem detached from the surroundings and preferably should appear indef-
initely localized. To accomplish this is not always easy; usually it can be only approx-
imated, especially for pictures viewed near by with binocular vision. It must be pointed
out, however, that with the proper attitude on the part of the observer, and in the absence
of distracting peripheral detail, the several psychological constancy phenomena tend to
correct small distortions of form, of size, and of the color-brightness relationships.
14-46
OPTICS
Right Eye
13. BINOCULAR VISION
Binocular vision is the coordinated use of the two eyes, in which a single perception of
external space is obtained, and by which the specific sensation of stereoscopic depth per-
ception is made possible. The final
perceptual images from the two eyes
are normally said to fuse in the brain,
and through the strength of the fusion
impulse all movements of the eyes
become coordinated in the process of
fixating different points in space.
One differentiates between the bin-
ocular visual field, which will cor-
respond to that portion of visual space
for which the images of the two eyes
will overlap, and the binocular field of
fixation which is the maximum field
swept over by the movements of the
two eyes. Figures 24 and 25 illustrate
the approximate angular dimensions
of these fields.
The luminosity of objects is some-
what increased by the use of two eyes
over that of only one, depending upon
a ^ ^ experimental conditions. Also the
100 visual acuity of two eyes is usually
PIG. 24. The Binocular Visual Field (after Southall,
Introduction to Physiological Optics)
Left Eyi
Field
found to be higher than that of one eye.
FUSIONAL AREAS. When the
eyes are fixated upon one point in
space, not all other points in space are perceived single. In fact, only those points will be
seen single that are situated within a certain three-dimensional region determined by the
distance of the fixation point and by
Region of Single
Binocular Vision
the equivalent anatomical extent of
certain areas on the retinas (Panum's
fusional areas). See Fig. 25. Points
in space outside these areas would
ordinarily be seen double (physiologi-
cal diplopia); however, unless atten-
tion is called to them, one is usually
suppressed. The functional extent of
Panum's area varies to some extent
with visual conditions, and its meas-
urement of size decreases somewhat
with practice. The size increases
away from the foveas toward the pe-
riphery. Near the fovea its minimum
extent is about 6 to 12 minutes of arc
in the horizontal meridian and about 6
minutes of arc in the vertical meridian.
All objects beyond a fixation point at
about 50 ft from the observer will gen-
erally be seen single. Double images
exert compulsion in nervations for the
eyes to move so as to overcome the
doubling. In the horizontal meridian,
the actual eye movements, however,
are usually subject to the will.
STEREOSCOPIC VISION. Stere-
oscopic vision rests upon the fact that
each of the two eyes, by virtue of
their separation,* sees objects in the
visual field from a slightly different
Inferred Cortical -^
Coansctions--^/
FIG. 25. The Spatial Region of Single Binocular Vision
and the Geometrical Relations for the Disparity of Reti-
nal Images in the Two Eyes
* The variation of the interpupillary distance, in the general population, is between 55 and 75 mm,
•with a median at about 63 mm (measured while the eyes are looking at a distant object).
BINOCULAB VISION
14-47
point of view, and hence the two retinal image patterns arc slightly dissimilar. See
Fig. 26. The angular separation of the retinal images, arising from two points ia
space, will be different in the two eyes, if one of the points is farther away from the ob-
server. This difference in angular separation defines a disparity between the images. A
disparity must always relate to two points in space. Referring again to Fig. 25, the double
images from points at A and beyond are said to be uncrossed disparate with respect to the
images of F, for if the right eye is suddenly closed the right half-image vanishes. Similarly
the images of points at B and nearer are said to be crossed disparate with respect xo the
images of F, for if the right eye is suddenly closed the left half-image vanishes- Between
the points A and B there will be some position for which the images from the two eyes
will not be disparate, either crossed or uncrossed with respect to the Image of F. Tins
criterion defines the position of points on the horopter surface. Stereoscopic depth per-
ception arises by virtue of the disparity between retinal images, uncrossed disparity being
associated with the sense of distance away from the fixated point. Objects seen in crossed
disparity are seen nearer than that point. Stereopsis is a specific sensation resting upon
, Pyramid In Space
R.E,
FIG. 26, Illustration of the Difference in the Image Patterns of the Two Eyes in Binocular Space
Perception
the physiological and anatomical organization of the retinal elements of the two eyes. It
usually occurs immediately for almost instantaneous illumination, and it exists within
the entire binocular visual field.
The angular disparity between the images of two separated objects in depth in space
will increase with the separation of the eyes and will decrease with their distance from
the eyes. Though a sensation of greater depth will be associated with greater disparities
of the images, the effect is not rigidly geometrical. For a given angular disparity, the
apparent depth interval, to be quantitative, must vary with the square of the vis-
ual distance.
The visual acuity of the poorer eye must ultimately limit the threshold of stereoscopic
vision. Likewise, the threshold of stereoscopic vision will depend upon those factors
influencing visual acuity and, like visual acuity, will vary with the duration of the stimuli.
For central vision and for durations longer than 3 sec, maximum acuity is obtained; for
shorter durations down to 0.2 sec there is a 4 to 5 fold increase hi threshold, after which
the instantaneous threshold is nearly constant (Langlands).
Although varying with interpupillary distance and with individuals as well as with the
nature of the detail in the visual field, the limiting threshold for stereopois frequently is
taken, on the average, as 30 seconds of arc. There is, correspondingly, a visual distance
beyond which objects at greater distances cannot be seen stereosoopicilly. This limiting
distance will roughly be 450 meters, or about a quarter of a mile. Under certain condi-
tions, when the threshold of stereopsis may be as low as 6 seconds of arc, this distance will
be exceeded several times* For the peripheral regions of tlie retina, this limiting distance
will be much reduced, owing to the lowered aexiity.
Two points separated vertically will have images in the two eyes which are vertically
disparate if those points are located to the right or left of the plane perpendicular to the
interpupillary base line. Vertical disparities do not give rise to the perception of depth,
as do horizontal disparities, but they undoubtedly aid in the spatial localization of objects.
14-48 OPTICS
Since the invention of the stereoscope by Wheatstone in 1838, and the discovery of the
bases for stereoscopic vision, various instruments have been devised whereby stereoscopic
views could be obtained with pictures. In general, the procedure consists in presenting
slightly different pictures or drawings before the two eyes which would correspond to the
views that each of the eyes would perceive if they had been present when the photograph
was taken. The devices include the mirror- and prism-stereoscopes, the haploscope, the
red and green and polaroid anaglyphs, grid devices, and even motion pictures where the
left- and right-eye views are projected alternately. The problem of projecting pictures
for stereoscopic vision, so as to preserve correct disparity relationships and the correct
perspective features, is a difficult one, especially for a group of observers (Rule) .
RIVALRY. If the fields presented to the two eyes are greatly different, for example
in radically different colors or in detail, instead of fusion or even a simultaneous percep-
tion of both patterns taking place, retinal rivalry occurs. In this, either one field or the
other is seen, usually alternately. In the case of dissimilar patterns sometimes sections of
each are seen simultaneously, but seldom both in the same region of the visual field. The
period of alternation of the two visual fields varies between 2 and 12 sec, depending upon
differences in luminosity, area, distinctness of detail within the fields, and central or
peripheral vision. One field may prevail over the other for longer periods if there is a
great difference in luminosity, or if intelligible detail exists on one and not the other, etc.
Ocular dominance may also be a factor in the field that prevails the longer. Only in the
case of certain color differences can fusion and therefore the emergence of a mixed color
arise.
BIBLIOGRAPHY
General
Eelmholtz, H. v., Physiological Optics, Eng. trans, by J. P. C. Southall. Optical Soc. Am. (1925).
Duke-Elder, W. S., Text-Book of Ophthalmology, Vol. 1. Kimpton, London (1932).
Polyak, S. L. The Retina. University of Chicago Press (1941).
Walls, G., The Vertebrate Eye. Cranbrook Institute of Science, Bull. 19 (August 1942).
Southall, J. P. C.t Introduction to Physiological Optics. Oxford University Press (1937).
Emsley, H. H.t Visual Optics, 3d Ed. Hatton Press, London (1944).
Bartley, S. H.t Vision, A Study of Its Basis. Van Nostrand (1941).
Guilford, J. P., Psychometric Methods, Chapters IV-VI. McGraw-Hill (1936).
Luckiesh, M., and F. K. Moss, The Science of Seeing. Van Nostrand (1937).
Hardy, A. C., Handbook of Cplorimetry. Mass. Inst. of Technology (1936).
Moon, P., The Scientific Basis of Illuminating Engineering, Chapter XII. 'McGraw-Hill (1936).
Woodworth, R. S., Experimental Psychology, Chapters 22-26. Henry Holt (1938).
Herirfg, E., Raumsinn, Hermans Handbuch d. Physiol. d. Sinnesorgane. An English translation, Spatial
Sense and Movements of the Eye, C. A. Radde. American Academy of Optometry, Baltimore (1942).
REFERENCES
Asher, L., Monoculares und binoculares Blickfeld eines Emmetropen, Arch. f. Ophth., Vol. 48, 427-
431 (1899).
Bond, M. E.t and D. Nickerson, Color-order Systems. Munsell and Qstwald, J. Optical Soc. Am.,
Vol. 32, 709 (December 1942).
Cobb, P. W., The Influence of Pupillary Diameter on Visual Acuity. Am. J. PhysioL, Vol. 36, 335
(1915).
Cobb, P. W., and F. K. Moss, The Four Variables of the Visual Threshold, J. Franklin Inst., Vol. 205,
831 (June 1928).
Cobb, P. W., and F. K. Moss, Glare and the Four Fundamental Factors of Vision, I.E.S. Trans., Vol.
23, 1104 (1928).
De Silva, H. R.. An Experimental Investigation of the Determinants of Apparent Visual Movement,
Am. J. Psych., VoL 37, 461-501 (1926).
Dohner, D. R., and C. E. Foss, Color-mixing Systems. Color vs. Colorant Mixture, J. Optical Soc.
Am., Vol. 32, 702 (December 1942).
Duane, A., Studies in. Monocular and Binocular Accommodation, etc., Am. J. OphtJial., 3rd Series,
Vol. 5, 865 (1922).
Engstrom, E. W., A Study of Television Image Characteristics, Pt. II, Proc. I.R.E., Vol. 23, 295 (1935).
Freeman, E., Anomalies of Visual Acuity in Relation to Stimulus-distance, /. Optical Soc. Am., Vol.
22, 285 (1932).
Hecht, S., Quantum Relations of Vision, /. Optical Soc. Am., Vol. 32, 42 (January 1942).
Hecht, S., Relation between Visual Acuity and Illumination, J. Gen. PhysioL, Vol. 36, 335 (1915).
Hecht, S., The Visual Discrimination of Intensity and the Weber-Fechner Law, J. Gen. PhysioL, Vol.
7, 235-267 (1924).
Hecht, S., The Nature of the Photoreceptor Process, Chapter 14, Murchinson's Handbook of General
Experimental Psychology. Clark Univ. (1934).
Hecht, S., and E. U. Mintz, Visibility of Single Lines, etc., J. Gen. PhysioL, Vol. 22, 593 (1939).
Hecht, S.r and R. E. Williams, The Visibility of Monochromatic Radiation and the Absorption Spec-
trum of the Visual Purple, J. Gen. PhysioL, VoL 5, 1-33 (1922).
Jones, L. A., The Fundamental Scale for Pure Hue and Retinal Sensibility to Hue Differences, J.
Optical Soc. Am., Vol. 1, 63-77 (1917).
Helley, K. L., Color Designations for Lights, /. Optical Soc. Am., Vol. 33, 627 (November 1943).
Klein, G. S., Relation between Motion and Form Acuity in Parafoveal and Peripheral Vision and
Related Phenomena, Arch. PsychoL, Vol. 39, 1-69 (October 1942).
ELECTRON OPTICS
14-49
LB(ial7)!8t N" M" S" Ezperiments on Binocular Vision, Tran* Optical Sac. Lwds>n, VoL 28, 4S-I03
1 SensitK'ities to C°l°r Differences in Daylight, J. Optical to. 4«., VoL 32,
>c. ,1m,, VoL 34,
M605\0ctober?9^)
?ro?1?'
Data Applied to
- MuMdl CoiOT Co., Baltimore (1929).
esolution as a Function of Intensity and Exposure Time of the
Vo1' 34' 73S December 19445.
- of y-io- *««*« °f Color Vision,
r
^TT nsities of Ugfat, J. Optical Soc. 4m., Vol. 4, 35 .
+L'n" S?*11' The Relative Merits oM&d and Whdt« Ugfat of Low Intimity for
' Efekn^ss' ^. O^icol 5oc. Am., Vol. 34, 601 (OctoberT944).
*»•• VoL ^ 313-322 (1938); also The Shape of
wHr ?•" ^"^an Y151^11 and $e Spectrum, Sc&netf, Vol. 101, 653 (June 29, 1945).
Walls, O., factors m Human Visual Resolution, J. Optical Soc. Am., V<^ 33, 489 (September 19431.
OsST' Indlrect Vjsusl Acuity, Zeitechrift /fir Ps^, u^f PA^u^. ^. ^innwswg., Vc^. 7, 172
N L
ELECTRON OPTICS
By D. W. Epstein
GENERAL CONCEPTS. Electron optics has become a branch of applied physics.
The term "electron optics" was chosen because of the similarity between the path of an
electron, or any charged particle, moving through electrostatic and rnagnetostafcie fields
and that of a ray of light passing through refracting media. Because of this similarity,
such concepts of optics as lens and focal length may be transferred to electrostatic and
magnetostatic fields.
The subject of optics is generally divided into: (1) geometrical optics, which treats only
of the geometrical relations of the propagation of light; and {2} physical optics, which,
utilizing the wave theory of light, is capable of dealing with any problem in light. A simi-
lar division is made in electron optics. This chapter will concern itself exclusively with
non-relativistic geometrical electron optics of static fields; that is, relativity, wave mechan-
ics, and electron optics of high-
frequency phenomena will be
excluded.
The analogy between electron
optics and light is indicated in
Figs. 1 and 2. Figure 1 shows
the trajectory of a ray of light
refracted and reflected at a
spherical interface separating
two regions of different indices
of refraction. The analogous
electron optical case is shown in
Fig. 2. Assume that by some
means (such as two closely
spaced meshes at different elec-
trostatic potentials) a space in
vacuum is divided into two
regions by a spherieocylmdrical . fr.^^f ± * J-D^^J*
<mrffloP as shown in Fit? *> the FIG. 1. Trajectory of a Ray of Light Refracted and Beftecied at
surface as shown m Jfig. -, tne & Splierical interface Separating Two Regions of Different
region to the left of the spherical Indices of Refraction
surface being at the electrostatic
potential Vi and the region to the right of the spherical surface being at the electrostatic
potential Vz- An electron emitted with zero initial velocity by a cathode (located to the
left of the Vi region) at zero potential will move in the Vi region at a constant velocity f i
given by
v^'1 meters P61 sec
kg is
where e = 1.59 X 10~19 coulomb is the charge of the electron and m = 9.04 X
its mass. As long as the electron stays in the region of constant potential Vi there is no
electrostatic force acting on it and it will move in a straight line, say OP in Fig. 2; this
corresponds to the law of rectilinear propagation in light optics.
14-50
OPTICS
When the electron crosses the spherical surface at P its velocity is changed to 02 cor-
responding to F2, i.e., to z>2 = 5.95 X 105 Vvl meters per second. The force being normal
to the surface, only the component of velocity VR normal to the surface will change; the
tangential component of velocity VT will be the same on both sides of the surface. It thus
follows (see Pig. 2) that
VT = 0i sin i — #2 sin r \«)
where i and r are the angles of incidence and refraction, respectively,
also be written
Vvl sin i — Vr^i sin r
or
Equation (2) may
(3)
so if NI and #2 are identified as the indices of refraction of the left region and right region
respectively and N as the relative index of refraction then eq. (3) becomes the well-known
law of refraction. The focusing
properties of a spherical refract-
ing surface then follow as indi-
cated in Fig. 2.
If F2 < Vi, then e(V2 - Fi)
is negative, and if in absolute
magnitude it is greater than
!/2 TO (t»i cos i)2 — the part of
kinetic energy of the electron
corresponding to the normal
component of its velocity — then
the electron will be shot back
from the surface with its nor-
mal velocity component re-
versed. The path of the re-
flected electron will make with
the normal to the surface the
same angle i which its path
made on incidence (see Fig. 2).
Thus the law of reflection also
holds in electron optics.
The different rays of a beam
of light do not affect one an-
other. The various electrons
in an electron beam repel one
another; this, of course, is the
well-known effect of space
charge. However, for low elec-
I VP-VI 1 > f- OT tei cos
FIG. 2. Electron Optical Analogy of Pig. 1
tron beam intensities the effect of space charge is negligible, and it will be so assumed in
what follows.
It is generally customary to deduce the laws of geometrical optics especially for non-
homogeneous media from Fermat's principle of shortest optical path.
This principle states that the path of a ray of light from a point A to a point B is always
such as to make the integral an extremum (usually a minimum) with respect to all neigh-
boring paths for rays of the same frequency. The principle is usually stated as
N ds = 0
(4)
where N, the index of refraction, may be a function of direction as well as position and ds
is an element of path length.
In particle dynamics there is the similar principle of least action stating that
r
d f
J A
pds = 0
(5)
where p is the momentum of the particle. A comparison of eqs. (4) and (5) shows that
an electron in an electrostatic and magnetostatic field will follow the same trajectory as
light would if the index of refraction at every point were made proportional to the momen-
ELECTROSTATIC LENSES 14-51
turn of the electron at the point. The momentum of an electron moving in an electrostatic
and magnetostatic field is
p = me — e A cos 6
where 0 is the angle between the direction of motion of the electron and the direction of
magnetic vector potential A. The index of refraction for an electron moving in a com-
bined electrostatic and magnetostatic field is
N = k \v - — A cos 0 (6)
Equation (6) shows that owing to the magnetostatic field A" is a function not only of the
position of the electron but also of its direction of motion so that combined electrostatic
and magnetostatic fields behave like non-homogeneous anisotropic media.
It was noted in Fig. 2 that the index of refraction for an electron at a point in an electro-
static field is proportional to its speed at the point, i.e., -V — Jb?, but it must not be assumed
that the index of refraction in a magnetostatic field is ke/mA cos 6 but rather
k tJ0 - — A cos B\ (7)
where VQ is the constant speed with which the electron moves through the magnetic field.
14. ELECTROSTATIC LENSES
The electrostatic lens of Fig. 2 is an example of a relatively impractical case. Practical
electrostatic lenses are generally formed by the application of electrostatic potentials to
axial symmetric electrodes. Figure 3 shows a cross-section through the axis of such an
electron focusing system. The double lines represent cylindrical, hollow conductors at
the potentials V\ and V*\ the single
lines represent the equipotential g 8000080
surfaces in the space (vacuum) be- £ £i 2 2 £* ™ S S
tween the electrodes. From eq. (3) \ \ \ / / / 7
it follows that each equipotential
surface represents a surface of con-
stant index of refraction. Here are
shown only a few of the equipoten-
tial surfaces; actually, of course,
there is an infinite series of equi-
potential surfaces having a com-
mon axis. This electron focusing FIG. 3. Equipotential Line Plot in Charge-free Space Due to
system may, therefore, be con- Potentials Applie4 to Coaxial Cylindrical Electrodes
sidered as a very large number of
coaxial refracting surfaces. Most optical systems for light consist of a series of spherical
refracting surfaces having a common axis of symmetry called the optic axis. For light,
the optical systems are usually such that the index of refraction changes abruptly as light
passes from one medium to the other. In electron optics, the index of refraction is a con-
tinuous function of position. Optically speaking, this means that an electrostatic field
constitutes an isotropic non-homogeneous medium for electrons, corresponding to a me-
dium of continuously variable density for light rays.
The potential distribution V(r, z) — the potential at a radial distance r from the axis
and an axial distance z from the origin — in charge-free space due to potentials applied to
axial symmetric electrodes is given in cylindrical coordinates by the Laplace equation
<fr» r dr dz*
subject to the boundary conditions that V(r, z) at the electrodes assumes the values of
the potentials applied to the electrodes. Except for some special cases it has not been
possible to obtain mathematical solutions subject to the actually existing boundary condi-
tions. The solutions are generally obtained experimentally by means of an electrolytic
tank. The potential distribution of Fig. 3 was thus determined.
The equations of motion of an electron moving in a meridian plane, i.e., a plane contain-
ing the axis, are
(r, a)
dr
14-52 OPTICS
The trajectory of a meridional electron traversing an axially symmetric electrostatic field
V(r, z) and with a velocity v — \/2(e/m)V(r, z), namely, an electron emitted with zero
velocity from a cathode at zero potential, is given by the differential equation
dV(r, z) dr
d2 2V(r, z) 62 d2 27(r, 2) dr
The distribution of potential in space is uniquely determined if the distribution along
the axis together with its even derivatives are known. Thus
V(r, 2) = 7(0, 2) - 7"(0, z) + V^CO, *) + ••• (10)
where V(Q, z) is the distribution of potential along the axis, "F"(0, z) is the second deriva-
tive of axial potential with respect to 2, YIV(0, 2) is the fourth derivative, etc.
It may be shown by using eq. (10) that the equipotential surfaces in the neighborhood
of the axis are hyperboloids with a radius of curvature of
This shows that, in electron optics, index of refraction and curvature cannot be varied
independently as they can in light optics. Consequently, the correction of some lens
aberrations is extremely difficult if not impossible in electron optics.
An optical system is usually described in terms of paraxial or first-order imagery. Actual
imagery departs from paraxial imagery. Such departures are described as aberrations.
The focusing action of an electrostatic field is similarly described to a first approxima-
tion by considering only paraxial electrons. Paraxial electrons are characterized by the
fact that in calculating their paths it is assumed that their distances from the axis, r, and
their inclination toward the axis, dr/dz, are so small that the second and higher powers of
r and dr/dz are negligible.
The differential equation for the trajectory traversed by a paraxial electron becomes
from eq. (9)
+jr"
iv»r-o (13)
4
where Vt V, and V are the axial distribution of potential V(Q, 2) and its first two deriva-
tives with respect to z respectively. Equation (12) or its equivalent eq. (13) may be taken
as the fundamental equation of paraxial electron optics of axially symmetric electrostatic
fields.
The general solution of the second-order differential equation (12) or (13) may be written
r(2) - cin(2) + C2r2(2) (14)
where r\(z) and r2(2) are any two linearly independent solutions and Ci and c2 are arbitrary
constants. Equation (14) states that the trajectory of any paraxial electron is simply the
linear combination of two independent trajectories. Hence the complete paraxial focus-
ing action of an axially symmetric electrostatic field is determined by calculating the
trajectories of only two electrons. The trajectories of two electrons entering the lens
parallel to the axis from the object and image sides are chosen as the two solutions 7-1(2)
and ri(z) and are called the two fundamental trajectories. These trajectories determine the
location of the cardinal points of the focusing system, i.e., the location of the focal and
principal points, and thus the focusing action of the lens.
Referring to Fig. 4 let Si and 8% be two equipotential surfaces such that the space to
the left of Si is equipotential and is at potential Vi and the space to the right of S% is equi-
potential and at the potential V^ The potential in the region between Si and £3 varies
continuously, as shown in Fig. 3. Then the paraxial electron moving parallel to the axis in
the equipotential space to the left of Si will follow the trajectory 7-1(2) and after passing
through the focusing system will move in a direction inclined at an angle to the axis and
will pass through the axial point -FV All paraxial electrons moving parallel to the axis in
the Vi or object space will pass through F%. The point ^2 is the second focal point. The
plane passing through the second focal point and perpendicular to the axis of symmetry is
the second focal plane.
ELECTEOSTATIC LENSES
14-53
The plane perpendicular to the axis and passing through the point of intersection of the
original and final directions of motion of the electron is the second principal plane. The
point of intersection H 2 between the second principal plane and the axis is the second prin-
cipal point. The distance H*FZ denoted by /* is the second focal length.
Similarly, a paraxial electron moving parallel to the axis in the T% or image space will
after passing through the focusing system move in a direction inclined 10 the axis and will
:ond Focal
.Second Focal Point
FIG. 4. Fundamental Trajectories and Cardinal Points of an Electrostatic Lens
pass through the point FI in the object space. FI is the first focal point. Fi may also be
considered that axial point in the object space from which all electrons, after passing
through the focusing system, are parallel to the axis in the image space.
The plane perpendicular to the axis of symmetry and passing through the first focal
point is the first focal plane. The plane perpendicular to the axis and passing through the
point of intersection of the original and final directions of motion of the electron is the
first principal plane. The point of intersection, J5Fi, of the first principal plane and the
axis is the first principal point.
It is to be noted that in Fig. 4 the principal planes are crossed. This is a characteristic
of lenses having indices of refraction different on the two sides.
In Fig. 5 let AiBi be an object (say, an aperture through which electrons are passing)
located in the equipotential region Vi. Then a paraxial electron coming from AI and
moving parallel to the optic axis will after passing through the lens go in the direction
F*A*. A paraxial electron issuing from A\ in the direction AiFi will after passing through
the lens move parallel to the optic axis and will intersect the trajectory of the other electron
at Az- Similarly the trajectories of all paraxial electrons coming from A\ will intersect at
A 2, the image of A\. The same is true of every point on AiBi, and so the inverted image
FIG. 5. Image Formation in a Direct Bipotential Electrostatic Lens
j, is obtained. The ratio AzB»/AiBi or h*/hi gives the magnification. The electron
image of AiBi becomes visible if a fluorescent screen is placed in the plane of A^BZ.
From eq. (12) or (13) and Fig. 5 it may be shown that the following relations hold:
& - \m (15)
(16)
/i +
•+;
/*
+ </i -
tfc - .
(17)
14-54 OPTICS
...
7F" LP + C/i — -
gi
(20)
2 „ (F2 - /a) - fz(m - 1) (21)
The complete paraxial focusing action of an electrostatic lens is determined by means of
the above relations when the positions of the cardinal points or /i, /2, -Fit and F% are known.
Electrostatic lenses are classified according to (a) electrode symmetry, (6) thickness,
and (c) the potentials on the sides of the lens.
Spherical lenses are formed by applying different voltages to two or more electrodes
having axial symmetry such as apertures and cylindrical and conical tubes. Spherical
lenses are used in cathode-ray tubes, television pick-up tubes, and electron microscopes.
Cylindrical lenses are formed by applying different voltages to two or more pairs of
electrodes having a plane of symmetry such as pairs of wires or pairs of strips. Cylin-
drical lenses are used in some receiving and transmitting tubes.
Thick lenses are characterized by the fact that the axial extension of the electrostatic
or refracting field is of the same order of magnitude as or even larger than the focal length.
It is necessary to know the positions of all four cardinal points in order to determine the
focusing action of a "thick lens.'*
Thin lenses are characterized by the fact that the axial extension of the refracting
field is negligible compared with the focal length. In a thin lens the principal planes
coincide, and the focusing action of the lens is determined by its location and focal lengths.
For estimating purposes it is sufficiently accurate to consider most lenses "thin."
The focal lengths of a "thin" spherical lens may be calculated from the relations
(22)
where V\ and Vz are the potentials of the equipotential regions on the two sides of the
lens, y and V the axial distribution of potential and its first derivative with respect to z,
and the integral is taken over the axial extension of the field.
Equations (22) also apply to "thin" cylindrical lenses, if the numerical factor 3/16 is
replaced by 1/2-
Unipotential lenses are characterized by having identical equipotential regions on the
object and image sides, Vi — Vz, and hence /i = —ft. Figure 6 shows a few electrode
arrangements and axial distributions of potential of unipotential lenses. Figures 7 and 8 *
give the focal length of several thin unipotential lenses as a function of Ve/Vo. The dotted
curves of Fig. 8 give the focal length of a unipotential lens where the central aperture has
been replaced by a fine metal screen or an electron-permeable conducting membrane. It
should be noted that this lens is divergent, i.e., fz is negative, when Ve/Vv is less than unity.
In the case of thin unipotential lenses eqs. (15) to (21) simplify to
A - -h (150
XiXz - -/a2 (160
i-i = ^ (180
Q. P h
» = r = !-=-^ = ! = ii = - (wo
1 3 fVi\X r* (V'\* .
7*~iS(v) L (v)dz
1 3 fV*\X /•& (V'\ ,
*--ieU; L (v) dz
p = -f*(r^r) (20°
5 = -Mm - 1) (210
* Figures 7 and 8 ware plotted from data calculated by Dr. E. G. RambergW RCA Laboratories.
ELECTROSTATIC LENSES
14-55
Vi V?
Vl
FIG. 6. Electrode Arrangements and Axial Distribution of Potential of Some Unipotential Lanses
14
2 12
!
\
i/s
JJ
'©
E
0 10
•c
u
0 1W
°1
* t: s
.J3 0 °
l<
2« ft
V
0
V
I
\
a
d
3
\
K
«I.
J*S 4
I
:
1
Z->
H
T
T
a
a
o 2
/
f
1
1
X
^
^
£ Z
/
•rO.4-0.20 0.4 0.8 1^ 1.6 2.0 2.4 2.8 3.2
Vg _ Voltage Applied to Central Electrode
Vfl Voltage Applied to Outer Elictrodes
FIG. 7. Variation of the Focal Length (Measured as the Number of Diameters of the Central Aperture)
with the Ratio of the Voltages Applied to the Central and Outer Electrodes
O.S 1
1,4 1.8 2.2 2.6 3,0 3.4
, Voltage Applied to Central Electrode
= Voltage Applied to Outer Etecirodes
FIG. 8. Variation of the Focal Length (Measured as the Number of Diameters of the Outer Electrodes)
with the Ratio of the Voltages Applied to the Central and Outer Electrodes. The solid curves apply to
system (a) with a small central aperture. The dotted curves apply to system {&) with a central elec-
trode consisting of a fine metal mesh or an electron-penaeable conducting membrane.
14-56
OPTICS
Bipotential lenses are characterized by having different equipotential regions on the
object and image sides, or Vi 7^ V*. In the direct bipotential lens the potential of the image
space is greater than that of the object space (Vz > 7i). In the inverted bipotential lens
V-2 < V\. Figure 9 shows a few electrode arrangements and axial distributions of poten-
tial of some bipotential lenses. Figures 10a to lOe give the focal lengths and positions of
Vi
FIG. 9. Electrode Arrangements and Axial Distribution of Potential of Some Bipotential Lenses
the focal points (thus giving the positions of the four cardinal points, see Fig. 5) as a func-
tion of Vz/Vi for 5 different diameter ratios d%/d\. Figure 11 shows /i, /2, FI, and F% as a
function of dz/di for V%/Vi — 5.
The focusing characteristics of a "thick" bipotential lens are given by eqs. (15) to (21).
Their use in conjunction with Fig. lOc will be illustrated by the following simple example
(see Fig. 5 for sign convention). Given the lens with d^/d\ = 1.5, V%/Vr~ 5, then, from
Fig. lOc, /i - -2.1dlf CFi - /O = -l.ldi, h = 4.7<*i, and (F2 - /a) = -1.8^. It is
desired to obtain a real image of an object with a magnification m = — 5 (since a real
image of an object is inverted). Then by eqs. (20) and (21)
-f 4.7di(-5 - 1)
and thus the object is located at a distance of S.Gdi to the left of the cylinder ends and the
image 26.4^i to the right of the cylinder ends.
3456789
.Vs _ Voltage Applied to Right Cylinder
Vi Voltage Applied to Left Cylinder
3 q
TJ g
vi
V2
c °
% 7
' ^
.^
— »-+
Id*
£ 6
\
L d2
— i
\
di
o
m 4
\
\^
c
X
X
CL
E
co 2
^^^.^
Q
— 1
F:
"T
— —
— —
o •*•
/
1
F
«
^i****
s „
^
^
Fy&7
1-5
0
•2-7
3456789
_Vg_ Voltage Applied to Right Cylinder
Vi Voltage Applied to Left Cylinder
(a)
G. 10. (See facing page.)
ELECTROSTATIC LENSES
14-67
€iU
"" 9
1 8
fi 7
vl 1 *
»
3 q
\ > i i i i
\ ; ' v.
td. ^- -^
i i
fr
1 8
o ^
i.
, Vi i „ .,-„- , „ ^
N ±1
AH , di
1"
£ l i1
. b
•5 5
2 4
0
« 3
§ „
v\ *i
\ X ,
3 b
\ \ / / — ^ i-
~^:_:^^:
o
\. \ ^1 — "^4— — i—
\ "t^-
i —
— ~^~
* —
4
V
t? ^
! ""^^-J i
^"-^_
•
E 3
j pyd'^ |
Constants In Number of DU
* m *>• ui ro i-> o H» h
Fa/d
Q
1 I
/°i-
0
\ \
/v&i
— —
— . —
j1 -^
—
1
/J
/oi
Z 2
£
^^^ ^-^— — -i
/ ^*~ ryd
l
^-4
/^ ^^fT^ 1 1
/
/ ix^ iJl !
Q
/ i
5
s c
' \
£ 3 4 5 6
w Vs _ Voltage Applied to F
789
Ight Cylinder
jeti Cylinder
&345678S
V«_ Voltage Applied to Right Cylinder
Vi Voltage Applied to Left Cylinder
Vi Voltage Applied to I
14
13
12
c 9
6 8
~ E
1 *
I 3
S 2
i-i
\
Vl
\
*--{-
A
tdi—
Ts-
\\
V
\
Ti
\
\
= 3.6
f
>
y N
S/Vtf
\
^•*>J^
\
"^s
fyd,
:.
1-3
"Si
t>
*^
- — •
S
/
^
*%
C3
o 7
-8
/
/
/
/
/
1
(
3456789
Va Vottage Applied to Right Cyf lodef
Voltage Applied to Left Cylinder
(c)
FIG. 10. Variation of Focal Lengths, /, a&d Distance of Focal Poinfes f rom End 1 oj ^Oygnder/-
as the Number of Diameters of the Cylinder on the Left), with^the Ratao of the Voltages
Eight and Left Cylinders
14-58 OPTICS
In the case of a "thin" bipotential lens eqs. (18) to (21) simplify to
-f a) f*
(18*)
m- \
fl + a
(20")
q - -a - Mm - 1) (21")
where a is the distance between the position of the equivalent thin lens and cylinder ends
as indicated in Fig. 5.
Bipotential lenses are most generally used in cathode-ray tubes.
Cathode qGrfd fAnode
0*0.2V +Y
00 V
1234.
ds__ Diameter of Right Cylinder
di~" Diameter of Left Cylinder
FIG. 11. Variation of Focal Lengths, /T and Distances
of Focal Points from End of Cylinders, jP (Measured as
the Number of Diameters of Cylinder at Left), -with the
Ratio of Diameters of the Bight and Left Cylinders
0-0.2V
FIG. 12. Electrode Arrangement and
Approximate Distributions of Po-
tential (for Three Values of Grid Bias)
of One of the Most Commonly Used
Cathode Lenses
Cathode lenses are characterized by having a plane of zero potential (cathode) normal
to the optic axis. The cardinal points of a cathode lens are of less significance than in case
of the other lenses because of the distribution of initial velocities of the electrons emitted
by the cathode. Figure 12 shows the electrode arrangement and approximate distribution
of potential of one of the most commonly used cathode lenses. Figure 12 also shows the
approximate trajectory of an electron emitted normal to the cathode for grid voltages of
+0.2, 0, and —0.2 V. The grid is so named since it is also used for controlling the cur-
rent going to the anode aperture. The cathode lens is the most widely used since it exists
in all types of electronic devices.
Electrostatic lenses suffer from the defects or aberrations known as spherical aberration,
coma, astigmatism, curvature of field, distortion, and chromatic aberration. They also
suffer from defects due to misalignment and maleonstruction of electrodes, space charge,
relativity effect, etc.
Spherical aberration is in general the most troublesome, especially in instruments re-
quiring a fine focused spot (or line) as in cathode-ray tubes, television pick-up tubes, and
electron microscopes. Figure 13 shows the increase in spot size caused by the spherical
aberration of a bipotential lens. The increase in spot size is given as a function of the
beam diameter at the end of the first cylinder measured in terms of the first-cylinder
diameter. Figure 14 shows the decrease in voltage ratio required to focus a beam of
MAGNETOSTATIC LENSES
14^59
tK^nf ff v" + ?-Ti h€ spherical aberration of the unipotential lens is greater than
!?*„ fi blfotentmi k?8, ?"* the equldiameter bipoiential lens has Jess spherical aber-
ration than a lens with (d.Jd,} > I or <*/*) < 1. In general the aberrations in electron
lenses are much more severe than they are in
light lenses (this also applies to magnetos* atie
lenses). This is primarily due to the connec-
tion between radius of curvature and index of
refraction — see eq. (11) — which exists in elec-
tron optics and not in light optics.
1500
I
1400
V?
V-
J
S1300
f1
— =:
—i —
— — -.
3
c
-J
!)
4.
3
•51200
<Zf>
_i
rr
wnon
di
= 1
b
rt
Si ooo
^ 900
)
/
£ 800
/
g 700
/
£
«= 600
^
0>
£ 50°
/
I 400
/
/
w
300
/
200
^
/
100
—- —
^
.0 0.1 0.2 O.3 0.4 0.50.6 0.7 0.8 0.9 1.0
d _ Beam Diameter at End of First Cylinder
d-L Diameter of First Cylinder
FIG. 13. Increase in Spot Size Caused by t&e
Spherical Aberration of a Bipotential Lens as
a Function o! the Beam Diameter at the End
of the First Cylinder
0.90
S 0.80
a
0.70
S0.6O
<3
^0,50
o 0.40
i^~^4^i i !
!
i ^>-<^ !
^^s^
i
* 0.30
20.20
>0.10
0,00
0.
i
j : i l
j
i
1
!
i !
! ! 1
0 ai 0.2 03 0,4 0.5 0.6 0.7 Q.8 0.9 1.
FIG. 14. Decrease in Focusing Voltage Ratio
Caused by the Spherical Aberration of a Bipo-
tential Lens as a Function of she Beam Diam-
eter at the End of the First Cylinder
15. MAGNETOSTATIC LENSES
Any axially symmetric magnetostatic field acts as a "lens" for electrons. Such fields
are generally created by passing direct current through coils with axial symmetry.
As already noted, a magnetostatic field is an electron-refracting medium whose index
of refraction is a function not only of position but also of the direction of travel of the
electron. Consequently magnetostatic lenses differ in then- behavior from electrostatic
and ordinary light lenses. In general the differences are made evident by a rotation of
the image and the irreversibility of object and image. ThusT a real image, produced by a
magnetostatic lens, is not inverted (as it is in an electrostatic lens), but is rotated through
an angle 6 relative to the inverted, image. Similarly, if the image is made the object, then
its image will not coincide with the original object (as it would in an electrostatic lens)
but will be rotated through an angle 28 relative to the original object. Magnetostatic focus-
ing is generally accomplished by long or short lenses. The image rotation of a magnetosattic
lens is, for a given focal length, reduced as the extent of the field along the axis is reduced.
Thus the image rotation is practically zero for aa extremely short lens and is 180° (image
erect) for a very long lens.
The long lens generally extends over the entire length, of the electron beam and is formed
by the uniform field of a long solenoid. It is used in such television pick-up tubes as the
image dissector, orthicon, and image orthicon. The uniform field of the long lens produces
a sequence of uniformly spaced, real, erect (rotation 180°) images with unity magnifica-
tion of an object which is placed normal to the field and which emits electrons of uniform
speeds. This follows from the fact that an electron injected into a uniform magnetostatic
field, B, with a speed v, and a corresponding voltage V and at an angle a with the field,
describes a helix, the radius of the helix being
flsina 3.38 X 10~s
(fl/m)B
- sin at meters
(23)
H
-meters
14-60
OPTICS
The time taken by the electron in describing 1 revolution is *
_ 2x 3.56 X 1CT11 2.84 X 10~s
B
H
(24)
(e/m)B
which depends exclusively on B or H and is independent of V or ex. The pitch of the
helix or the distance that the electron has traveled in time T is
21.1 X IQ~*\/V cos a ,
: meters \
27rtj cos a.
(e/m}B
- meters
(25)
If the angles a. at which electrons from a point source are injected into the field are small,
then, their speeds along the lines of force, » cos a, are essentially constant (cos a. — 1)
and all electrons will reunite at the following distances from the source
21.1 X 10"6nV7
B
H
meters
(26)
where n is an integer. Since any line of force is an axis of symmetry in a uniform field,
an extended electron-emitting (or "illuminated") source placed perpendicular to the field
will be imaged at the distances sn of eq. (26) (see Fig. 15) .
Object
[ O O O Q O O O Q O O O Q Q O Q O O O OOOOOOOOOOO OOP O CM
-H HH
FIG. 15. Image Formation by a Uniform Magnetostatic Field
The short magnetostatic lens extends over a limited region of the beam and is generally
formed by the non-uniform field of an iron-encased coil with a narrow slit in the iron shell
or pole pieces (Fig. 16). Short lenses are used in electron microscopes and television
FIG. 16. Short Iron-dad Magnetostatic Lens and Approximate Distribution of Axial Flux Density
cathode-ray tubes. Except for some image rotation the short lens behaves like a thin
uni|M>tential electrostatic lens so that its focusing characteristics are given by eqs. (150
MAGNETOSTATIC LENSES
14-61
to (21'). The focal length of a short lens is given by
2.2 X 1010 f
V Ja
3.5 X IO-2 t
meters"
meters
(27)
where B is the axial component of the flux density along the axis of the lens, and V is the
potential of the equipotential region in which the lens is located.
The image rotation is given by
8 m
radian*
= 0.19 r*>
~ */vJa '
H dz radians
(28)
Integrating eqs. (27) and (28) for a wire loop of diameter d and carrying a current ATI
results in
/a 8 X W^V V
d 37r3(e/m)(ArJ)2 .V2!2
10~
NI
(
'V?
(29)
(30)
To a fair approximation, eq. (29) also applies to a short coil of mean diameter d, of N turns,
and carrying current /. Figure 17 is a plot of eq. (29) giving, graphically, the focal length
4 6 S 1O 20 4O 60 80 1OO 2OO 400 600 1000
FIG. 17. The Focal Length of a Short Coil as a Function of Ampere-turns and Beam Voltage
as a function of voltage and ampere-turns. Figure 17 may be used, for estimating pur-
poses, in the case of an iron-encased coil if the ampere-turns are small and if d is taken as
14-62
OPTICS
the clear diameter of the pole pieces. Since the iron-clad coil concentrates the field more
than the air coil, the iron coil produces the smaller image rotation.
Besides the usual 5 third-order aberrations of spherical aberration, coma, astigmatism,
distortion, and curvature of field, the images produced by magnetostatic lenses usually
suffer from three other aberrations. These are generally known as anisotropic distortion,
anisotropic curvature of field, and anisotropic coma. Anisotropic distortion is often
called the "S effect/' since this aberration distorts a straight radial line on the object into
an elongated letter S on the image.
16. ELECTRON PRISMS
A uniform electrostatic field and a uniform magnetostatic field constitute the two basic
types of electron prisms. Electron prisms are used for deviating (deflecting) beams of
electrons of uniform speed as in cathode-ray tubes and pick-up tubes, and for dispersing a
beam of charged particles so as to separate particles of differing mass or speed as in the
ion trap of a cathode-ray tube and mass spectrograph.
Electrostatic prisms are generally formed by the approximately uniform field between
the charged plates of a condenser (see Fig. 18) .
FIG. 18. Deviation (Deflection) of an Electron Beam by an Electrostatic Prism (Deflecting Plates)
A charged particle moving initially perpendicularly to a uniform electrostatic field, 13 ,
with a velocity v (corresponding to a potential drop V}, follows a parabolic trajectory while
in the field. On leaving the field the charged particle is deviated into the direction of the
field (see Fig. 18) through the angle a given by
tan ce. •
__
2V ''
IVd
'' 2dV
(31)
where I is the extent of the field or approximately the length of the plates, d the distance
between the plates, and Vd is the difference in potential between the plates. The apparent
center of deflection is located approximately at 1/2 from the ends of the plates, and the
amount of deflection at the distance L from the center of the plates is
ILVd
(32)
Magnetostatic prisms are generally formed by the approximately uniform field between
two current-carrying coils or pole pieces of a magnet.
Ifca, 1$. DeTiati©D. (BefleotioiL) of an Electron Beam by a Magnetostatic Prism (Deflecting Coils)
REFERENCES 14-63
A charged particle moving initially perpendicularly to a uniform magnetostatic field
with the velocity t> follows a circular trajectory in a plane at right angles to the field. On
leaving the field the charged particle is deviated in a direction perpendicular to the field
(see Fig. 19) through the angle a given by
\/7]mlB
sin a. = - _ (33)
Vzv
which becomes in the case of electrons
sin a = 2.97 X 105 -^L (34)
vv
The apparent center of deflection is located approximately at the center of the field, and
the amount of deflection at the distance L from the center of the field is
IT 5
h - L tan a S 2.97 X 105 -^ (35)
17. GENERAL THEOREMS ON ELECTRON OPTICAL SYSTEMS
Electron optical systems generally consist of a cathode lens and one or more electrostatic
and/or magnetostatic lenses and electron prisms (deflecting plates or coils).
The following general theorem applies to an electron optical system using electrostatic
and magnetostatic elements. The trajectory of a charged particle remains similar, as long
as the quantity (e/m}(BzLz/V] is kept unchanged. Thus, if the voltages on all the elec-
trodes are increased by a constant factor n, it is necessary to increase B by the factor Vn
in order to keep the trajectory the same. If all the linear dimensions (L) of the system,
i.e., of all the electrodes, coils, object distance, image distance, etc., are increased by the
factor n, it is necessary either to increase all the voltages by n? or to decrease B to l/n
in order to keep the trajectory similar.
The following theorems apply to any purely electrostatic electron optical system:
1. The trajectory is independent of e/m. Hence all like charged particles emitted by a
cathode will be identically focused and deflected by any electrostatic optical system.
2. The trajectory of any charged particle emitted by a cathode is unchanged if the
voltages on all the electrodes are increased by the same factor.
3. If all the linear dimensions of all the electrodes are increased by a constant factor n,
the trajectory remains unchanged (if measured in units n times larger).
All electron lenses which are free of space charge and conductors within the field of the
lens and are bounded by uniform potential regions on both sides are always convergent,
i.e., will form a real image of an object located beyond the focal point of the lens.
The maximum current density, /a, obtainable in an electron spot or image, regardless
of the electron optical system employed, is given by
where J"i is the specific emission of the cathode, kT is the initial kinetic energy of an elec-
tron emitted by a thermionic cathode at the absolute temperature T,k = 1.38 X 10 "^ erg
per degree, eVz + kT is the final kinetic energy, and az is the angle of maximum converg-
ence of the electron trajectory at the spot or image.
Equation (36) may be deduced from the fact that, for a perfect optical system which
accepts and focuses all the electron current emitted by a thermionic cathode, J* = Ji/m*
(m = magnification), and m = — Sm ai (see eq. [41], p. 14-08), where DI and t?2 are the ini-
$2 sin 02
tial and final velocities of an electron and «i(= 90°) is the angle of maximum convergence
at the cathode.
REFERENCES
1. Bruche and Scherzer, Geometrische Elektronenoptik. Julius Springer, Berlin (1934).
2. Maloff and Epstein, Electron Optics in Television. McGraw-Hill (193S).
3. Meyers, L. M.? Electron Optics. Chapman <fc Hall, London (1939).
4. Zworykin, V. K., et aL, Electron Optics and the Electron Microscope, John Wiley (1945).
SECTION 15
ELECTRO-OPTICAL DEVICES
PHOTORESPONSIVE DEVICES
AST. BT HERBERT E. IVES PAGE
1. Radiation, Properties, and Means of
Detection 02
2. Thermal Devices 03
3. Photoemissive Cells 04
4. Photoconductive Cells 11
5. Barrier Photocells 13
6. Photovoltaic Cells 15
7. Choice of Cells for Various Purposes 15
TELEVISION PICK-UP TUBES
BT V. K. ZWOBTKIN AND
E. G. RAMBEBG
8- Requirements 19
9. The Image Dissector 19
iQ. The Iconoscope . 21
11. The Monoscope 25
12. The Orthicon 26
13. The Image Orthicon 27
14. Fields of Application of Pick-up Tubes 29
LUMINESCENT AND TENEBRESCENT
MATERIALS
AST. * - PAGE
15. Preparation and Notation of Phosphors 32
16. Mechanisms of Phosphors ............. 34
17. Mechanisms of Scotophors ............ 36
IS. Specific Characteristics of Useful Phos-
phors and Scotophors ............... 37
CATHODE-RAY TUBES
BT L. E, SWEBLTTND
19. Electron Gun ........................ 41
20. Bulbs for Cathode-ray Tubes .......... 43
21. Characteristics of the Image ........... 44
22. Television Cathode-ray Reproduction
Tubes ............................ 46
23. Oscillograph-type Cathode-ray Tubes. . . 47
24. Cathode-ray-tube Displays (by T.
SOUJEB) ............... ...- ...... 49
15-01
ELECTRO-OPTICAL DEVICES
PHOTORESPONSIVE DEVICES
By Herbert E. Ives
1. RADIATION, PROPERTIES, AND MEANS OF DETECTION
Photoelectric tubes, or cells, belong to the general class of instruments responsive to
radiant energy, or radiation. An intelligent use of such instruments demands a knowledge
of the more important characteristics of radiation, which may be summarized as follows:
Radiant energy consists of electromagnetic waves, of a vast range of wavelengths, extend-
ing from radio waves, many meters long, to x-rays and y-rays less than a millionth of a
millimeter in length (see Section 11, article 5), The portion of this extended spectrum
which is effective in photoelectric tubes and similar devices is confined to a small region
centering around that group of wavelengths commonly called light, or the visible spectrum,
which extends roughly from 0.8 micron (1 micron = 10~4 cm) to 0.4 micron. (Other units
of measurement frequently encountered are the angstrom unit, 10"8 cm, and the millimi-
cron, 10~7 cm.) The adjacent region of longer wavelength is called the infrared; that of
shorter wavelength, the ultraviolet* The radiations in the visible spectrum vary greatly in
their ability to produce the sensation of light, the relationship between energy value, or
radiant intensity, and luminous value being indicated by the luminosity curve of the spec-
trum which has a maximum at approximately 0.5 micron, dropping to zero at the ends of
the visible spectrum. Radiant energy is measured in energy units, namely, ergs or joules;
and radiation or radiant flux is measured in ergs per second or watts: The irradiation of a
surface, such as that of a phototube, is measured in ergs per second incident per unit area,
or watts per unit area. Luminous flux is radiant flux evaluated according to its luminosity
(the integral of the product of the radiation spectrum and the luminosity curve of the
spectrum). Its unit is the lumen. One lumen is radiated in unit solid angle by a point
source of luminous intensity of 1 candle. The illumination of a surface is measured in
lumens incident per unit area. The meter-candle or lux is an illumination of 1 lumen per
square meter.
All instruments which respond to radiation do so because they absorb some of the energy
of the radiation and transform it into some form susceptible of practical measurement or
utilization. Thermal instruments become heated by the incident energy, and indicate
by changes of dimensions, position, or the production of electrical currents. Photoelectric
instruments depend primarily upon the fact that the incidence of radiation on matter
causes the emission or release of electrons, setting up electromotive forces or causing
electrical currents to flow.
CLASSIFICATION" OF PHOTORESPONSIVE DEVICES. It is convenient to divide
photoresponsive devices into two broad groups, namely, thermal devices and photoelectric
devices. In the group of thermal devices are included thermojunctions, bolometers, and
radiometers. In the group of photoelectric devices are included photoemissive cells, photo-
conductive cells, barrier photocells, and photovoltaic cells.
The thermal instruments in general respond to a wide region of the spectrum, correspond-
ing to the thermal absorbing power of the materials of which they are constructed or with
which they are coated. Since they are frequently coated with a "black" of high and sub-
stantially uniform absorbing power through the infrared, visible, and ultraviolet portion
of the spectrum they are often termed "non-selective." They are generally less sensitive
than the photoelectric instruments in the spectral region to which the latter respon'd; they
are much slower in response and, being usually of relatively low resistance, are not easily
adapted to methods of electrical amplification.
The 'photoelectric instruments are in general sensitive to relatively narrow regions of the
spectrum (are strongly selective), but they are far more sensitive in these regions than the
thermal instruments. They have also the great practical advantage that they are readily
adaptable to the various modern methods of electrical amplification.
15-02
THERMAL DEVICES
15-03
&'
1
t •
ii~j
1 *
1
I
t •
I
f •
I
r •
1
I
i *
1
i * -
Fro.
1. Linear
mopile
Ther-
2. THERMAL DEVICES
THERMO JUNCTIONS. When two different metals are joined and the junction is
maintained at a temperature different from the rest of the circuit, a potential is generated
whose magnitude is dependent on the temperature difference and on the materials of the
junction. When this difference is very small the potential will be proportional to the
temperature. Bismuth and antimony and some of their alloys give large potentials com-
pared with most other metals, and many thermopiles have been made of them. Good,
durable combinations of high sensitivity commonly used at present
are bismuth against silver, bismuth-tin against bismuth-antimony
alloys, and Constantin against Manganin.
Other requirements beyond high thermoelectric power are a low
internal resistance and heat capacity and low thermal conductivity
between the hot and cold junctions, and in practice a compromise
has to be made between these factors. Thermoelements are used
in three principal forms: the single junction, the multiple-junction
thermopile, and the radiomicrometer, the last being a galvanometer
with a thermojunction built directly into, and forming a part of, the
moving coil. Multiple junctions are preferable where the illumina-
tion extends over some area; for example, where spectral lines are
to be measured a linear arrangement of couples is often used, a dia-
gram of which is shown in Fig. 1. The warm junctions, a, which
receive the radiation to be measured, are commonly flattened or
covered with small, thin disks or squares of metal to present a large
receiving area. These disks are usually blackened, for instance, with
a layer of lampblack, in order to make them uniformly absorptive
to a long range of wavelengths. The connection to the cold junc-
tions, b and &', must conduct as little heat as possible and at the
same time not have too high an electrical resistance. In order to
secure the maximum stability it is desirable to shield these cold
junctions thoroughly from scattered radiation and to maintain their
temperature substantially equal to that of the walls of the sur-
rounding enclosure. This is accomplished by attaching fins of relatively large area to
the cold junctions.
The galvanometer should have a resistance not far from that of the thermopile, usually
from 10 to 50 ohms. There is no advantage in increasing the number of junctions beyond a
certain point, and in fact with a given flux the overall sensitivity may be the largest with a
few junctions of small heat capacity especially if they are enclosed in a vacuum which
eliminates the loss of heat by conduction and convection to the atmosphere and reduces
the disturbing effect of drafts. The sensitivity of thermopiles is expressed in volts per
unit of irradiation, in some cases, in terms of the response from a stated source at a given
distance, commonly a
Table 1. Sensitivity of Thermopiles Hefner candle at 1 meter.
Values for some of the
standard thermopiles are
given in Table 1,
For the sensitivity in
watts per square centime-
ter multiply the above fig-
ures by 107, and for gram
calories per second per
square centimeter multi-
ply by 4.186 X 107- One
Hefner standard lamp
with. 14 by 50 mm diaphragm opening gives, at 1 meter, 9.6 X 10~fi watt per sq cm or
9.6 X 102 ergs per sec per sq cm.
If a thermopile is to be used with weak radiation, as it frequently is, it is very important
that the thermopile and the galvanometer be adapted to each other in order to secure a
high sensitivity of the system, i.e., the ratio of the scale reading to the flux. Besides high
voltage sensitivity of the pile previously mentioned, other i^iiirements are that the
galvanometer should have a low internal resistance, high voltage sensitivity, and a critical
damping resistance equal to that of the pile inclusive of the leads. Such galvanometers
are made by the Leeds and Northrup Company, Philadelphia, and Kipp and Zonen,
Holland.
Ohms
Resistance
Volts per Erg
per Second per
Square Centimeter
Moll linear
20
0.75 X 10~8
"FTilger lin**ftf . , . T - - ,
10
0.7 X I0~8
Ivloll large surface
50
5 0 X 10~s
Moll sensitive vacuum couple. . .
Moll quick vacuum couple
Coblentz vacuum couple
45
20
14.8
0.46X 10~8
0.13 X I0"s
0.7 X NT8
15-04 ELECTKO-OPTICAL DEVICES
The sensitivity of the system can sometimes be greatly increased by concentrating the
radiation on the junctions and also by using one of the numerous optical devices for
amplifying the galvanometer deflections. These are arrangements whereby a light beam
reflected from the galvanometer mirror actuates a photocell, the output of which in turn
produces an increase in the deflection or operates a second galvanometer. In the Moll
thermorelay made by Kipp and Zonen, or the similar Zernike differential couple, the re-
flected light beam determines the relative temperatures of two opposing thermojunctions,
the net output of which controls a second galvanometer. In this manner the readings can
be increased up to the inherent instability of a galvanometer, but care must be taken to
preserve the linearity of the entire system.
BOLOMETER. The bolometer is essentially a sensitive resistance thermometer of very
small heat capacity; that is, the electrical resistance of a fine wire or strip of metal is
increased by the heating due to the radiation. It was used extensively before the develop-
ment of the modern high-sensitivity, quick-acting thermopile, which is more convenient
and stable under ordinary conditions. In its practical form two bolometer elements form
two arms of a Wheatstone bridge, which the radiation unbalances. It is essential that a
material such as platinum be used which has a high temperature coefficient of resistance
as well as a low heat capacity and conductivity. Unless unusual precautions are taken
the entire bridge network is subject to temperature fluctuations which render the readings
uncertain. The sensitivity of bolometers is about one-millionth of a degree per millimeter
deflection of a galvanometer used without intermediate amplification. For example, a
bolometer of 2,8 ohms resistance and using 40 mils current gave a deflection of 45 cm
when exposed to 1 candle at 1 meter with a galvanometer sensitivity of 1.5 X 10~10 amp
per mm, the scale being at 1 meter.
THERMISTOR BOLOMETER. A more recently developed form of bolometer is one
made of thermistor materials, that is, semiconductors whose resistance varies rapidly
with temperature. Combinations of oxides of nickel, manganese, and cobalt change their
resistance about 4 per cent per degree centigrade, or about ten times as much as platinum.
The oxides are prepared in the form of thin flakes cemented to glass or quartz. A typical
flake 3 mm long, 0.2 mm wide, and 0.01 mm thick has a resistance of 4 X 106 ohms and
with 250 volts applied gives a sensitivity of 300 volts per incident watt or 18 volts per
watt per sq cm. The spectral response is determined by the optical properties of the oxide
constituents, which may show regions of relative transparency in the infrared. Because
of the high resistance the output of the thermistor bolometer is well adapted to electrical
methods of amplification.
RADIOMETER. The Nichols radiometer is a self-contained instrument consisting of
two similar vanes of blackened mica or platinum on a horizontal arm and suspended in a
vacuum. It is a development of the toy known as Crookes' radiometer frequently seen
in optical shops, which consists of four vanes, each blackened on one face, on arms balanced
on a needle-point, which rotate when illuminated. The behavior of the radiometer is
dependent on the gas pressure; at higher values the blackened sides of the vanes are drawn
in turn toward the window; at lower pressures the warming of the blackened faces by the
radiation causes the residual gas molecules to rebound from their surface directly to the
cooler window and push the vanes away from it and the radiating source. All practical
instruments have the gas pressure so adjusted that they work by the latter method. The
Nichols radiometer is used by measuring the deflection of the vanes by means of a small
mirror attached to the cross-arm supporting^ them, its rotation being observed by the
usual telescope and scale. The sensitivity of the radiometer to radiation is of the same
magnitude as that of the bolometer with a sensitive galvanometer,
SPEED OF RESPONSE OF THERMAL DEVICES. The thermal devices are in
general slow to respond to variations in signal strength and hence are not well adapted for
following rapidly fluctuating radiation, such as radiation modulated at speech frequencies.
The time constant, defined as the interval in which the response declines to 1/e value, is
for the fastest devices of the order or 5 milliseconds.
3. PHOTOEMISSIVE CELLS
STRUCTURE. In photoemissive cells an electropositive metal surface is placed in a
highly evacuated enclosure, usually of glass or quartz, together with another metal plate,
the electropositive material constituting the sensitive cathode, the other plate the anode,
and both plates are connected with terminals led through the glass. The action of the
cell is as follows: When light falls on the cathode, electrons are emitted into the space
above. These pass over to the anode, and, if the terminals outside the cell are connected
through a current-measuring device, a current is observed which varies with the total
PHOTOEMISSIYE CELLS
15-05
illumination. Although some current will flow without a battery being connected in series,
it is common practice to use one, and then the cells act primarily as valves, tlie illumination
controlling the amount of current which is permitted to pass.
Practically all photoemissive cells use alkali or alkaline-earth metals as their light-sensi-
tive materials, and the structure is largely influenced by the problem of introducing these
metals into the glass or quartz enclosure. In early types of photoemissive cells an alkali
metal, such as sodium or potassium, was introduced in molten form into a simple spherical
bulb provided with one leading-in wire in contact with the pool of alkali metal^and a
to
Central Cathode Cell
Central Anode Cells
Jfehf
1 "f* 1
rTT'^^rt n .nYft. P7a ny.a j
* f&-f:-i'tt£x:£-??:*J%
selenium Conductive
Cell
CO
Voltaic Cell
FIG. 2. Types of Photo-responsive Cells
Photomultiplier Tube
second wire to serve as an anode. This type has been almost entirely superseded by cells
in which the alkali metal forms a thin film upon some other metal. Two general types
of structure are common, respectively, the central-anode and the central-cathode types.
The central-anode type is represented by cells (a) and (&), Fig. 2. In these the alkali
metal has been distilled upon a metal plate or on the walls of a bulb with an opening left
for a window for the light. The central anode consists of a wire loop or grid. The central-
cathode type, which is illustrated in (c), Fig. 2, consists of a metal plate, on which the alkali
metal has been deposited, more or less surrounded by a grid or metal covering on the bulb
wall serving as the anode.
ELECTRODE MATERIALS. The most commonly used photosensitive materials are
the alkali metals, sodium, potassium, rubidium, and cesium, whose intrinsic sensitiveness
increases in the order given. The sensitiveness of the pure metals is, however, far below
that of the same metals when given various special treatments, such as being exposed to a
glow discharge in hydrogen or being put down upon an oxidized base and given special
15-06
ELECTRO-OPTICAL DEVICES
54321
-f- Volfs on Cafhode
FIG. 3.
1234
— Volts on Cathode
heat treatments. The most generally used cell at present consists of a silver plate which is
oxidized and subsequently exposed to cesium vapor and heat treated. A later develop-
ment has been the combination of antimony with cesium, which produces a high sensitivity
localized in the blue region of the spectrum. Other materials, such as barium and cadmium,
are occasionally used when sensitiveness to particular regions of the spectrum is required.
VACUUM AND GAS-FILLED CELLS. Photoemissive cells are commonly made up
either as high-vacuum cells or as gas-filled cells. In high-vacuum cells, the photoelectric
current consists entirely of the elec-
trons emitted from the cathode. In
gas-filled cells, an inert gas such as ar-
gon is introduced at a pressure of sev-
eral tenths of a millimeter of mercury,
-^ and, when a sufficient voltage is ap-
plied, the photoelectrons by collision
with the gas produce ionization,
whereby the current is amplified sev-
eral times. This process of gas ampli-
fication is limited by the ignition volt-
age, at which a visible glow discharge
takes place, which is self-perpetuating
Current-voltage Relation for a Central Cathode an(} ^^ injure the surface of the
CeU cathode.
VOLTAGE-CURRENT CHARACTERISTICS. The relationship between voltage and
photoelectric current under constant illumination depends upon the physical structure of
the cell, particularly upon the size and arrangement of the electrodes. The structure
best adapted for studying the fundamental phenomena of photoelectricity is the central-
cathode arrangement. The voltage-current relation for a vacuum central-cathode cell,
in which the dimensions of the cathode are negligibly small compared with those of the
anode which encloses it as completely as is possible while allowing space for the entrance
of light and mechanical parts, is shown in Fig. 3. In this figure, the abscissas represent
voltages applied to the cathode and show that, at
a certain positive voltage, that is, with a field which
opposes the emission of electrons, the photoelectric
current makes its appearance. This point, which
is a measure of the maximum, energy given to the
photoelectrons by the incident light, is called the
"stopping potential.*' As the positive voltage is
decreased, the photoelectric current increases until
it reaches a steady value at the saturation voltage.
This voltage will be zero if anode and cathode are
of the same material, but it will be displaced by the
contact difference of potential between the anode
and cathode where the materials are different,
In Fig. 4 is shown the corresponding character-
istic for a vacuum central-anode cell. Here, be-
cause of the small target presented by the anode,
saturation is reached only at high voltages. In
Fig. 4 is also shown the voltage-current relation-
ship for a gas-filled cell of the same construction.
At low voltages this characteristic is essentially
that determined by the structure of the cell,
whether it be central anode or central cathode,
but at higher voltages the current increases rapidly
up to the ignition voltage of the gas which is, in
general, of the order of magnitude of several hun-
dred volts. Beyond this point, a sustained dis-
charge occurs with a negative voltage-current
characteristic.
ILLUMINATION-CURRENT RELATIONSHIP. With an ideal cell structure, the
number of electrons released by the light, and consequently the photoelectric current, are
directly proportional to the illumination. In all practical cells, however, this strict rela-
tionship is departed from to a slight extent because of charging effects of exposed glass
walls and other obscure phenomena. For this reason, photoelectric cells are applicable to
precision photometric measurement only if their exact characteristics are determined by
experiment, or if a substitution method is used. In gas-filled cells, the illumination-current
20
18
16
20 40
s_
7
60
Votts
80 100 120
FIG. 4. Current-voltage Relation for
Gas and Vacuum Central Anode Cells
PHOTOEMISSIVE CELLS
15-07
relationship departs from strict proportionality whenever, as is common, a high series
resistance is used either as part of the measuring system or for protection against the
occurrence of a glow discharge. The photoelectric current flowing through this series
resistance uses up part of the applied potential, thereby lowering the voltage across the
cell itself, which accordingly works upon a
lower point in the voltage-current character-
istic of Fig. 4. Typical illumination-current
curves for a gas-filled cell with various series
resistances are shown in Pig. 5.
WAVELENGTH RESPONSE. The photo-
electric current per unit of incident radiation
varies greatly with wavelength and in different
ways, depending on the characteristics of the
sensitive material employed.
Figure 6 shows the equi-energy response
curves for several typical cells compared with
the average eye. These exhibit maxima of
emission strongly localized in different parts of
the spectrum. The maximum lies in the blue
for the potassium hydride cell, in the infrared
for the cesium-silver oxide cell, and in the near
ultraviolet for the cesium-antimony cell. The
type of cell to choose for a given purpose to
secure the maximum response depends on the
characteristics of the light source used. Sources
like the tungsten lamp, whose emission is
greatest in the infrared, evoke a maximum
response from cells of the cesium oxide type,
as illustrated in Fig. 7, where two cells of Fig. 6
are excited by tungsten lamplight instead
of an equal-energy spectrum. Daylight and the quartz mercury arc, on the other hand,
evoke a greater response from cells whose sensitiveness is farther toward the blue end of
the spectrum.
SENSITIVITY. The luminous sensitivity of photoemissive cells is ordinarily defined
by their output in microamperes per lumen of steady light. For gas cells which have some
Fia. 5. Currenfc-iUnTnmatlon Relation for
Gas Cell with Various Series Resistances
Relative P.E. current per unit energy, maximum =1,0
ooo oopooppv
Jijb i-« Io wk 01 en vj bo 10 c
/ y
f\
,1
>-f
/
V
^
s
x
N
1
I
K
\
\y
\
\
/
\
CsO(
51,S5
)
j
1
I
f \
I \
!\
:\
/
\l
h
iRH
\
\ '
\
,
f
\
/I
1
i\
l\
y
i
!&
1
i
i
v
V
\
\
1
i
\
A
\
\
\
\
1
v
i
\
\\
*-
\
\
I
V
-"A
\
\
^
\
\
\
,
^
^
\
\
V-
\.
•~-»_-
\
X
^
•*- —
00 4000 5000 6000 7000 8000 9000 10,000 11,000 12,000
Wavelength, angstmm units
PIG, 6. Equi-energy Spectral Response for Some Types of Blue- and Red-sensitive Cells andjiihe
Average Eye
inertia at acoustic frequencies this sensitivity is often stated in terms of the cell's ability
to follow a sinusoidally varying light at one or more stated frequencies within this range.
In general the sensitivity depends on the cell voltage, the flux intensity and its color, the
resistance in the external circuit, and the distribution of the flux over the cathode if it is
15-08
ELECTRO-OPTICAL DEVICES
20
18
16
-12
£
010
§ 8
CsO
non-uniform, as it frequently is to some extent. No allowance is ordinarily made for the
glass bulb or any absorbing films on its interior as they must be tolerated in using
the cell.
Since the output is dependent on the spectral composition of the light, this should be
specified; as tungsten lamps are ordinarily used in rating cells, it is done by stating their
color temperature. There is no
general agreement on a standard
color temperature, but 287 0 deg
abs has been suggested and is used
by some manufacturers. Figure 8
shows how the sensitivities of the
red-responsive cesium oxide and
the blue-responsive potassium hy-
dride cells vary with this tempera-
ture. The sensitivity should not
be confused with the total output
obtainable from a cell as the fila-
ment temperature of the lamp is
raised; this output always increases
rapidly. The current per lumen of
light, however, decreases with
highly red-sensitive cells because
there is relatively less red to blue
or total light. Typical sensitivities
are given in Table 2.
The sensitivity of photocells is
also defined by the magnitude of
their response per unit radiant flux
_ _ at a given wavelength. For exam-
3000 4000 5000 6000 70OO sooo 9000 loooo uooo 12000 pie, the cells in Fig. 6 may be so
Wave-length - A° evaluated by their microampere
FIG. 7. Tungsten Spectral Response for KTT and CsO Cells output per microwatt of irradiation
at the wavelengths of maximum
response. Typical values for xinamplified commercial cathodes are: SI, 0.002 at 7500 A;
S2, 0.002 at 8000 1; 83,0.002 at 4400 A; S4, 0.04 at 3750 i.
In evaluating photoemissive cells the permanence and stability of the sensitivity must
be considered along with its absolute value. Commercial emissive cells are usually per-
manent and stable provided that excessive voltages are not used (particularly on gas cells)
c
o
I
\
\
Sensitivity In Microamperes por
5 8
\
^
^
"tX^Cej
ium
^-^
^^
^r—
^
^^
Potass
ium
2000° 4000° 6000° 8000° Abs.
Temperature of the Light Source
Fia. 8. Variation of Sensitivity with Color Temperature
and provided that they are not subjected to excessive heating or too concentrated illumina-
tion. Any ionization even of residual vapor or gas must be avoided for maximum stability
ao that in precision use anode voltages as low as 20 volts are recommended.
e, due to a conducting film around the stem or to thermionic emission from the
PHOTOBMISSIVE CELLS
15-09
cathode, may render high sensitivity more or less useless. Cathodes deficient in red
sensitivity, such as cesium-antimony, have greatly reduced thermionic emission.
FREQUENCY RESPONSE. The emission of electrons in the photoelectric effect is
practically instantaneous, and accordingly the emission should be capable of following
intermittent illumination
Table 2. Sensitivity of Photoemissive Materials
(Tungsten lamp source)
up to exceedingly high fre-
quencies, such for instance
as those required for tele-
vision. In practice, the
frequency response drops
off at high frequencies,
owing either to the pres-
ence of the gas in gas-filled
cells or in vacuum cells to
the presence of the high
series resistance, which is
ordinarily used for cou-
pling purposes, or to the
electrostatic capacitance
of the cell considered as a
condenser. Typical fre-
quency-response curves
are given in Fig. 9.
Microamperes
per Lumen *
Filament Color
Temperature,
deg Kelvin
Potassium hvdride
0 5-1 0
2848
Potassium-sulfur .
I 8
2848
Sodium-sulfur
"> 4
2848 j
Sodium-sulfur-oxygen . . ...
6-8
2848 i
Cesium antimony (34)
50-45
2870
Cesium oxide on. silver (S 1 , S2) ...
S3 ...
10-50
6 5
2870
2870
S5 . .
15 0
2870
S8
3.0
2870
* Intrinsic sensitivity of the cathode; amplification by gas or by sec-
ondary emission may increase these figures by several times or by sev-
eral orders respectively.
In a gas cell the frequency response is dependent on the applied voltage, and if this is
near the breakdown the loss of response may considerably exceed the values shown. It
is not advisable to exceed the voltage recommended by the manufacturer.
MEASURING CIRCUITS FOR USE WITH PHOTOEMISSIVE CELLS. There are
two general methods of measuring photoelectric-cell output: first, the measurement of
the current directly; and second, the measurement of the voltage drop across a series
resistance. The photoelectric current is measured by inserting a sensitive galvanometer
in series with the cell and a battery, and the method is limited in sensitiveness only by the
sensitivity of available galvanometers. The voltage drop across a high resistance is
measured by means of an electrometer or of special vacuum tubes designed to function in
the same manner. For extremely minute illuminations, the high resistance may be made
infinite, and the current may be ascertained by the rate at which the electrometer or
equivalent device charges up.
A number of d-c galvanometers are made which are suitable for use with photoemissive
cells, ranging in sensitivity down from about 10~10 amp; this can be extended to about
10 ~12 amp with a device like the Moll thermorelay. The resistance of the galvanometer
is immaterial, provided that it has a high current sensitivity, because the resistance of the
cell will ordinarily be enormously greater. It is not desirable for several reasons to use
an instrument that is much
more sensitive than the work
demands, but the testing of
various types of cells of widely
varying characteristics with
different colors and intensities
of iHurnination may require a
very flexible galvanometer
system. In this event, shunts
can be used if they are so ar-
ranged as not to interfere with
the critical damping. A good
method is to insert various
sections of the damping resist-
ance in the cell circuit. The
Leeds and Northrup type
22S5-F galvanometer is suit-
able for this purpose. Where
considerable current is available and portability is desired, microammeters of the Rawson
or Weston type are convenient, especially when provided with a dial or other means of
securing various scale sensitivities.
In all cases, great care must be taken to protect any instrument from a breakdown of
the cell by inserting sufficient series resistance, at the same time, if possible, retaining
linearity of response. For work of the highest sensitivity it is necessary to resort to an
LOO
%
50
20
0
2
— r~ ^^
>
Gas Cell
Vacuum Cell
DO 506 1000 20OQ 5000 1C,OOO
FIG. 9.
Frequency
Frequency Response for Gas and Vacuum Cells
15-10 ELECTRO-OPTICAL DEVICES
electrometer such as the Compton type, the applied potential being secured by the drop
across several megohms in series with the cell, or by using the cell as a constant current
source and measuring the rate of charging of the electrometer placed in series. Effective
use of the electrometer requires a permanent laboratory installation. Where greater
portability is desired practically equivalent results can be secured by amplifying the very
small currents by an "FP.54 pliotron" and measurement on a moving-coil galvanometer
such as the Leeds and Northrup type R. For the methods of using an electrometer see
Hughes and DuBridge's Photoelectric Phenomena, 1932, pp. 435-444, and for the corre-
sponding technique of amplification see DuBridge, Physical Review, Vol. 37, Feb. 15, 1931,
pp. 392-400. For descriptions of the more common electrometers see the catalog of the
Cambridge Instrument Company, and for galvanometers consult catalogs of Leeds and
Northrup Company and Kipp and Zonen.
AMPLIFICATION OF PHOTOEMISSIVE-CELL OUTPUT. Photomultiplier Tube.
The initial current produced by illumination of a photocathode may be greatly amplified
by utilizing the phenomenon of secondary emission. In the photomultiplier tube the elec-
trons emitted from the cathode are directed by a suitable high-voltage field onto another,
usually similar, electrode where they cause the emission of secondary electrons which are
greater in number than the impinging electrons. This process may be repeated a number
of times. Present commercial multiplier tubes have as many as nine such stages, and
even larger numbers have been used in special tubes. The overall current amplification
thus produced is of the order of several hundred thousand times. A typical electron mul-
tiplier structure is shown in (g), Fig. 2t and commercially available models are listed in
Table 3, p. 15-16.
Circuits for Amplifying Photoemissive-cell Output. The photoemissive cell, because
of its exceedingly high internal resistance, is admirably adapted for use in connection with
vacuum-tube amplifying devices. In the simplest arrangement, the electrometer described
in the previous section is replaced by the grid of a three-electrode tube, and the potential
acquired by it modulates the current through the vacuum tube, which may be further
amplified by successive stages.
Circuits for amplifying photoerm aai ve-cell output are determined by the type of appli-
cation of the cell. These can be put largely into three classes: trigger operation, d-c linear
operation, and a-e linear operation. The first class is concerned with merely a qualitative
response, and there is no particular requirement for linearity. A large number of uses*
come under this classification, such as the operation of relays in various counting and sort-
ing processes. The usual circuit for amplification consists in feeding the voltage drop
across the cell load into a thyratron tube which in turn actuates a relay (see Section 21).
The necessity for supplementary amplification will depend on the light variation available
and the marginal requirements of the relay. It is necessary to provide for the release of
the thyratron, and this can be easily done by using alternating current on its cathode or
interrupting the direct current. The sensitivity of trigger systems can ordinarily be in-
creased by the use of large load resistances in the cell circuit.
A method of use closely allied to the preceding in the characteristics demanded of the
cell is as a null device in substitution photometry, where the only requirement is a suitable
recorder with enough amplification to give the necessary precision. If the test and com-
parison lights are rapidly alternated on the cell, the method permits of a-c amplification
with its attendant advantages of great efficiency and simplicity, the match being given
by zero a-c output.
The second class, d-c linear operation, covers the direct-reading method of photometry,
an example of which is the recording of daylight intensity. This method has the disad-
vantage of requiring stable cells of reproducible, linear characteristics, a requirement not
always easy to meet for precision photometry. For many purposes, however, the require-
ments are not rigid and commercial cells are suitable for the purpose. Several methods
of amplification are possible. One is to use straight d-c resistance-coupled amplification,
preferably at low cell currents, with an electrometer tube as the first stage. In order to
minimise the tendency to instability inherent in d-c amplification, use is sometimes made
of balanced d-c amplification. At low light intensities these direct methods require much
care to guard against leakages in and around the cell, and, for some purposes, specially
constructed cells are necessary. Another precaution that must be taken is to insure the
linearity of response of the amplifier. A third method of amplification that is sometimes
applicable is to interrupt the illumination of the cell and use a-c amplification (see Section
7). This has the advantages of greater stability, of minimizing leakages, and of securing
the efficiency of interstage coupling by transformers.
Such uses of photocells as for picture transmission and sound pictures may be classed
as a-c linear operation. Here the response must be not only linear but also uniform over a
range of frequencies which may, as in television, be very large. This imposes certain
PHOTOCONDUCTIVE CELLS
15-11
restrictions on the load impedance in the cell circuit. Since a large value is necessary in
order to secure a high voltage output into the amplifier, the shunting capacitance becomes
very important and severely limits the useful value of the impedance that can be used-
Noise Limit to the Use of Amplification. Broadly speaking, any photoelectric current,
however minute, can by successive amplification be raised to any desired high value. A
limit is set to the effectiveness of this process by the noise in the cell or its associated
circuits, which is amplified along with the signal. The significant specification of sensitivity
of a photocell thus becomes the signal which can override the noise. Noise in a photocell
exists because of natural fluctuations of current at low values and by the thermal agitation
of electrons in the coupled resistances, and it is a function of temperature, frequency, and
band width. In addition there are many extraneous sources of noise from such causes
as the ionization in gas tubes, interference, microphonic contacts, power supplies, and
dielectric leakages. These can usually be diminished to secondary importance by careful
shielding and design of the circuits. Where considerable amplification of weak photo-
currents of wide bandwidth is required there will be a gain hi the signal-to-noise ratio by
using a multiplier phototube for the initial stages.
4. PHOTOCONDUCTIVE CELLS
The fact that light could directly change the electrical resistance of a substance was
first discovered about 1880 by observation of the effect in metallic selenium, and since
that time some 2000 papers have been published concerning its behavior and use. Never-
theless, the mechanism whereby light releases electrons remains obscure. Furthermore,
many of its characteristics depend to a considerable extent on the method of const rucrion
as well as the conditions under which they are measured. Two types of construction have
been used for such cells: one in which a thin layer of selenium is sandwiched between two
electrodes, one of which must be translucent to permit illumination of the layer; and one
in which two interlocking metallic grids or combs are bridged by a layer of selenium. Mod-
ern cells are usually of this second type, although the barrier cells described below use the
first. An example of a conductive selenium cell of comb construction is shown in Fig. 2(d ) .
Other materials which exhibit similar properties are thallium sulfide and lead sulfide. The
former is used in a cell known commercially under the name of "Thalofide." Both these
newer cells possess properties which render them superior to selenium.
Current-illumination Relationship. If a selenium cell is placed in series with a battery
and meter and is illuminated with increasing intensity, the resulting current will usually
be of the shape shown in Fig. 10. In general
the change in conductance, G, follows the
equation
where g and x are constants, F the light flux,
TQ the dark resistance, and r»- the light resist-
ance. The constant x is frequently about
0.5, so that the photocurrent varies approxi-
mately as the square root of the illumina-
tion. The dark resistances of different grid
cells vary greatly but usually are from
100,000 up to several megohms; those of the
sandwich type are much lower and may be
only a few hundred or thousand ohms. The
current-illumination relation of thallium
sulfide differs from selenium in not being
curved as strongly toward the illumination
axis.
Photoconductive cells are made to oper-
ate on a variety of applied voltages, and in
general the recommendations of the maker
should be followed. If not hermetically sealed the cells should be protected from excessive
moisture and corrosive gases such as sulfur fumes. High illumination also causes deterio-
ration of some cells.
WAVELENGTH RESPONSE. Typical curves of the spectral response for both selenium
and thallium sulfide are shown in Fig. 11. It is characteristic of the former to have a
peak at 7000 or 7500 angstroms, the sensitivity up through the visible region being variable
1
s
o
(
F*
^
^^^
^
i^— •"""
J^
;>-'
/
//
s
I/
/
j
312345678
Illumination
3. 10. Current-Illumination Response for Se-
lenium Conductive Cell
15-12
ELECTRO-OPTICAL DEVICES
with different cells and frequently rising again as the ultraviolet is approached. Thallium
sulfide is much more infrared-sensitive than selenium, with a maximum around 10,000
angstroms, after which it falls off rapidly, whereas lead sulfide has a maximum at 25,000
angstroms and falls to 20 per cent at 4000 and
33,000 angstroms.
FREQUENCY RESPONSE. Many oscil-
lographic observations have been made on
the speed with which the photocurrent builds
up when a selenium cell is suddenly 'illumi-
nated and on the rate of decay of the current
when the light is removed. This method of
observing its inertia, however, is ordinarily
not so useful as the method of measuring its
response to continuously interrupted light of
known frequencies. Figure 12 shows such a
measurement starting at very low and extend-
ing to nearly 10,000 interruptions per second,
the ordinates being the a-c response relative
to the flat portion as unity. The most re-
cently developed Thalofide cells fall off much
more slowly with frequency and are useful up
to the lower voice frequencies; the frequency
performance of lead sulfide is notably better than that of thallium sulfide, remaining
practically constant up to 5000 cps.
SENSITIVITY. Photoconductive cells are commonly rated by then* ratio of dark-to-
light resistance at a stated iUurnination and voltage. Thus a cell may be stated to have a
ratio of 6 at 100 ft-c using a bat-
tery of 100 volts. As there is
no agreement on a standard
light intensity or color, care
must be exercised in comparing
cells from different manufac-
turers. The d-c sensitivities
may be divided into two classes
according to whether the load
in series with the cell is a relay
to be operated directly, or a
resistance, the voltage drop
across which is in turn required
40OO 50OO 6000 7000 SOOO 9OOO 10000 11000
Wave-length
FIG. 11. Spectral Response for Selenium and
Thallium Sulfide Conductive Cells
0.1
0.01
0.001
i
i
1
T
_]_
I
' 1
OJ.
102 103
to operate the grid of a therm-
ionic tube. In the latter case
i 10
Frequency
FIG. 12. Frequency Loss for Selenium Conductive .Cell
the expression for the voltage sensitivity, a; of selenium is
dEe Eng __
where Es — voltage across load effective on grid.
E = battery voltage.
F = light flux.
TO = dark resistance of cell.
g = constant of the cell, its light conductance being g\/F.
Ti = light resistance of cell.
This is the equation for the maximum voltage sensitivity at light flux F, where the load
resistance is equal to the light resistance of the cell n, under the condition of operation.
If the load is a relay to be operated directly in series with the cell the ampere-turn sensi-
tivity must be used instead of the above. This is equal to the voltage sensitivity given
above multiplied by 1/i, where t is the resistance per turn of the relay.
If a photoresistance cell is operated between dark and a given light intensity as the
limits, the maximum voltage change across the load resistance, r«, is secured when
the voltage change being
Ttte same condition for ra applies for the current-turn sensitivity, and its change is equal
to tne voltage change multiplied by l/£.
-l ±_\
Ti -f ra r0 -f ra/
BARRIER PHOTOCELLS
16-13
AMPLIFICATION OF PHOTO CONDUCTIVE-CELL OUTPUT. The amplification
of the output of these cells is fundamentally the same as for the emissive cells, and the
same types of amplifiers can be used. Since conductive cells have much lower impedances,
it is possible in many cases to match the load to the cell and thereby secure the maximum
efficiency of operation. Since the cell resistance may vary rapidly with illumination, care
must be taken that the match be made at the average light intensity at which the cell is
to be operated. If an intermittent or variable illumination is used such that the cell must
respond to some range of frequencies it may be necessary to equalize the output in order
to preserve fidelity of reproduction. Since there is an increasing loss as the frequency of
response is increased, it is necessary to compensate for it by introducing attenuation of
the lower frequencies by a filter network at some convenient point in the amplifier. The
highest frequency at which one desires to work will then determine the effective loss of a
cell.
5. BARRIER PHOTOCELLS
STRUCTURE. The fact that, under certain conditions, photoconductive selenium
cells could produce an emf on illumination without any applied potential has been known
since the late nineteenth century. The discovery of the effect in cuprous oxide revived
interest in it and led to the development of cells of commercial importance. They are of
the sandwich type of construction referred to above and illustrated in Fig. 2(e). A photo-
sensitive material such as selenium or cuprous oxide C is formed on a suitable metallic
base E and covered with a translucent conductor such as a wire mesh A or a thin metallic
film. If the photosensitive layer is itself partially transparent, as, for example, cuprous
oxide, a photo emf may appear at junction D, where it is called a "back-wall effect," or
at B, where it is called a "front-wall effect."
The location and degree of sensitiveness are
dependent on the method of preparation,
the heat treatment, rate of cooling, gas con-
tent, and treatment of the boundary sur-
face. If an attempt is made to pass current
across such a photosensitive boundary by
inserting a battery of a few volts in the
meter circuit, it is customarily found that
the current can flow much more easily in
one direction than in the other, and this di-
rectional resistance behavior or rectification
is illustrated in Fig. 13 for a typical com-
mercial cell in the dark, the unit here being
of the front-wall type. As a photocell with-
out the external battery, the effect of illumi-
nation is to make the top become negative
and the base positive; that is, the electrons
released by the light flow in the high-resist-
ance direction. If the active layer is at the
back wall D, Fig. 2(e), the behavior is pri-
marily the same except that the polarities
are reversed with respect to the top and bot-
tom. In this case the light must penetrate
much more material, which reduces the
optical efficiency and alters the spectral re-
sponse curve.
10000
9000
7000
54000
3000
1OOO
I
i
7
-2 -1
Top-hE
0
Volts
2
Top-E
FIG. 13.
Dark Resistance-voltage Relation for
Selenium Barrier Cell
When a barrier cell is illuminated, its dark resistance at zero applied voltage is decreased
by the photoconductive effect in the layer, and at high intensities it may be much reduced
for a cell of the characteristics shown in Fig. 13.
ILLUMINATION RESPONSE. The current-illumination response of a typical cell
is shown in Fig. 14 with various series resistances. With very low resistance or short-
circuited current the relation is linear or very nearly so, gradually becoming more curved
as the resistance is increased until the open-circuit voltage relation is reached. Figure 15
shows the two extremes for comparison. Care must therefore be taken not to use too
much series resistance if a linear response is desired.
WAVELENGTH RESPONSE. In Fig. 16, A shows the spectral response for a typical
selenium cell; B and C are for front- and back-wall cuprous oxide cells, respectively. In
general, cells of this type have most of their sensitivity in the visible region. Back-wall
cells of cuprous oxide, however, are deficient in this region owing to the absorption of the
15-14
ELECTRO-OPTICAL DEVICES
red oxide so that their response is confined largely to the visible red and some distance
beyond into the infrared. Cells equipped with optical filters to make their response closely
that of the eye are now supplied by manufacturers.
40 SO 120 160 200 240 280
Illumination in Foot-candles
FIG. 14. Current-illumination Relation of
Barrier Cell with Different Series Resistances
200
360
320
280
240
200
160
120
80
40
. — '
.--•
180
ft
^
N<$
/
160
'^
s
/
/
/
140
/
/
,
/
/
"°i/-in
\l
/
.>ioc
&
z
1
&
/
80
^
/
60
/
/
/
/
/
/
0
°
40 80 120 160 200 240
Illumination - Foot-candles
Fia 15. Short-circuit Current and Open-
circuit EMF-illumination Relations for
Barrier Cell
SENSITIVITY. Barrier cells are rated according to their microampere-per-lumen
output, and the same qualifications apply to them as were stated for emissive cells con-
cerning the color of the light source and resistance in series. On account of the warping
of the linearity of the current curve by comparatively small resistances, care must be taken
in its measurement to use a sufficiently low-resistance meter. It is also frequently useful
in certain applications to have a statement of the open-circuit voltage in millivolts per
lumen. From Fig. 15 it is clear that this ratio is high at low illuminations and rapidly
diminishes as the illumination is raised, and for this reason it is necessary to state the
illumination at which the measurement is made.
Calculations of the maximum power and voltage sensitivities are complicated by the
fact that the internal resistance decreases with illumination, especially with the selenium
type. For this reason, it is necessary
to know the characteristics of the in-
dividual cell, and it is advisable to
consult the manufacturer regarding
the particular use to which it is to be
put or to determine the proper load
experimentally. For the cuprous ox-
ide type the internal resistance is com-
monly assumed constant, and in this
£0.8
LJ
^0.6
I
"£0.4
/
s>
V
X
s
\^
/
A
\
\
{/
\\
,
\
/i
\
\
y
I
\
\^
/\
E
3/
y
s
'
\
\
/I
\
9
^ s
V
,
^^
X
>
V/
^y
'
X
case the maximum voltage sensitivity,
dEg/dF, is equal to Sr, 5 being the
sensitivity constant and r the internal
resistance, the load, rz,, being rela-
tively very large. In this case the
maximum power sensitivity is ^VF/2,
where rz, = r. These values of TL will
ordinarily be sufficient to cause depar-
ture from linearity of current response
so that a compromise must be made by sufficient reduction in the load resistance. Barrier
cells are liable to deteriorate, and direct-reading instruments utilizing them such as
foot-candle and photographic exposure meters should be checked occasionally and the
eel replaced if necessary. Poor contact with the romping rings may also develop. This
30OO 3500 40OO 4500 5000 55OO 60OO 6500 7000
Wave-length
FIG. 16. Spectral Response of Barrier Cells. A, sele-
nium. Br cuprous oxide, front wall. C, cuprous oxide,
back wall
CHOICE OF CELLS FOR VARIOUS PURPOSES 15-15
type of cell is subject to a fatigue which causes a decrease in the response when first
illuminated. Recovery takes place in the dark, but the reproducibility of readings is
somewhat dependent on the duration and intensity of illumination. This type has no
dark current.
FREQUENCY RESPONSE. Exact information on the various commercial cells is
not available. Barrier cells have a relatively large internal capacitance which diminishes
their output with increasing frequency. The "Photronic cell" is stated to give a satis-
factory response to light interrupted at 60 cycles per second, and if this output is assumed
100 per cent then at 120 cycles it will be about 5S per cent, at 240 cycles 30 per cent,
and at 1000 cycles 6.4 per cent. It is also stated that, if an equalized response is produced
up to 5000 cycles, the power level is reduced approximately 35 db. The response of the
cell to single interruption is more rapid than that of a relay, so that for this use they may
be considered instantaneous.
AMPLIFYING CIRCUITS. If constant illumination is to be used, a d-c amplifier is
demanded, which may be troublesome to build and operate. In general it is therefore
recommended that the light be interrupted at a low frequency of, for example, about 60
cycles, and that a good a-f amplifier capable of transmitting this frequency efficiently
be used.
The remarks previously made concerning the amplification of emissive and conductive
cells also apply to this type. Barrier cells have lower impedance than either of these, and
are well within the range of practical transformers, so that they can be directly coupled and
the output used in an a-c amplifier. Equalization of frequency response may be necessary
as with the conductive cells.
6. PHOTOVOLTAIC CELLS
In the middle of the nineteenth century it was discovered that if two similar electrodes
of certain materials, such as platinum or silver coated with silver halide, were immersed
in dilute electrolytes and one electrode was illuminated, a voltage appeared between them.
These are referred to as photovoltaic cells, although some writers broaden this name to
include also the barrier cells previously described and refer to them as wet and dry cells
respectively. Various combinations of electrodes, coatings, and intervening liquids have
been employed, but, apart from experimental studies of the effect, the usual materials are
oxides, sulfides, or halides in an acid or inorganic salt electrolyte. Cuprous oxide gives a
large effect and has frequently been used in attempts to commercialize this type, the non-
sensitive electrode being some durable material such as lead with an electrolyte of lead
nitrate in water; see Fig. 2(/).
CHARACTERISTICS. The behavior of the open-circuit voltage and the short-circuit
current responses with illumination for a cell of the Cu, Cu^O, PbCNOaK Pb construction
are similar in shape to the corresponding characteristics for barrier cells (see Fig. 15) , the
former showing a tendency to voltage saturation and the latter being linear. The effect
of increasing external resistance is also qualitatively similar; see Fig. 14.
The spectral response of the cuprous oxide cell is high in the visible spectrum, being a
maximum in the blue or blue-green.
These cells are subject to polarizing effects which make them more unstable than the
other types, and there is a gradual deterioration of the sensitive layer which greatly
shortens then* useful life. It is claimed that this deterioration can be inhibited to some
extent by using a depolarizer such as hydrogen peroxide in the electrolyte to oxidize the
free hydrogen which reduces the cuprous oxide.
The response to illumination and the recovery afterward are not as rapid as the cuprous
oxide barrier effect.
7. CHOICE OF CELLS FOR VARIOUS PURPOSES
Although the applications of photocells are frequently classified according to marginal
or linear operation, this does not have so much to do with the choice of the cell as the
method of its use and of the amplification of its output. Ordinarily the selection of a cell
is dominated by considerations of high sensitivity to tungsten or daylight, the requirements
of precision photometry, a particular spectral response, or convenience, all of which
involve the relative evaluation for the purpose at hand of such factors as magnitude of
output, frequency loss, fidelity of color and intensity response, permanence, stability,
leakage, and absence of external battery.
15-16
ELECTRO-OPTICAL DEVICES
^
o
fi
I
3
6*36*o'l
d
.2
'S'S'
mum
ampe
M
mic
Maximum
Operating
Volts
Typical
Sensitivity,
microamperes
per lumen
Sil lll
G !_< j-i *r| Ji fi _
f-.oa; i3 oo^-^m
<y a ao u a a g S a
e^^° rt rc3rc3ggd
0
OOOJO
ft p, ft C.
— .cot- .
xxx
^oooooo o — o o o o o
OOO*AOOO O^ — C\O^O^CT»Os
«r\4n«ntStr»u*v«n |
Q Q
» ^ , pd
o «s o ^ c5^ o o so »A o »n «n u^ O m o §
ts »— CN T -«-«Nes >r-^-<*<Ncs \oinsj
tq pq -u%
"
~
P SS S^"
— \o — •<«• — ««j-r»ir<i«'0k'^»-— •* «— c^ — i— r4 — — —
QG CQ OQ OQ 02 GC db CO QQ CC QC CQ O2 CQ QQ OJ CQ CQ CO DQ
coooooo
••• '<
CHOICE OF CELLS FOR VARIOUS PURPOSES 15-17
Rauland
Westinghouse
Westinghouso
G.E. Co.
G,E. Co.
§§§!
Weston
Weston
Selenium Corp.
G.E. Co.
G.E. Co.
ers see Electronics
lable: A/13 « 36,
nfrared response:
Tapered Small 4-pin
410
4101
M8-074
3313
ill
Prong
Threaded
2-pin for radio sockets
Unmounted
"3,
"o
"1
(9
erage sensitivity are ava
or typoS rated as longer i
1
S3 d
0
C
cS ^3
>
VS-
sS
ac ^
0
*- n
, * ,
0
§ •=
c
0000
t=l
c
0 0
rv,
o
1 ob
£ §
1
0 GO 00 »0*
O o" O* -~ -*J
i** GO 00 23
**** CA eft >< «
S • ^ *
.2 .2 * "
"d
1
o
i
"S
1
mensions. Three
bes. In some oas
?d
Cro
ll
o
*S ^
wr
"3 t£
rC *
00000
0000
3
t 0
§J
~~ "~ "~" ~~
1
•E Q
S^
t< 03
0
J3 0
2 »2
»n r* in «n «>«»
to us 0
*- 2SS
"XXX
A'l
talogs should be
difference is in
00 for gas.
iviolei response
of the code.
e. This and ot
75, WL789 by ^
00 CO CO GQ DQ
"o
I
P
CQOQ zaoQ
33333
representative samples ; ca1
name Cetron. The major
/B « 300, C - 160, D «*» 3
he deep red and near ultrt
uaily measured regardless
violet-transmitting envelop
1 are WL707, WL773, WL7
feSiSS
1
,->
fill
ss
03 IE 03 00 OD
cj OS e3 o3 cj
_ft_ft_ft_ft
C3 03 O QJ flj
•C 'S 'H *C "C
^ i+ i* t- t^
{Sffiftpfi
rely to give i
3113
1 ll
• £K
available in
et tubes not
S
4^7l§§
. § °
111
o o "
1
^ g " 5-g e.
Il =
§||
<j -^ ri GO
^J t>* fS tN,
s s^SS
.25
H
i'^sP'
15-18 ELECTRO-OPTICAL DEVICES
The cesium oxide cell is particularly efficient for use with, tungsten light because its
maximum sensitivity is near the optimum energy emission of the high-brilliancy gas
lamps. This renders it suitable for sound pictures, telephotography, television, and numer-
ous marginal applications such as counting and control operations. The color response
is also sufficiently extended over the spectrum to permit its use in many sorting operations
and in colorimeters. In some technical applications it is necessary or, at least, highly
desirable that the cells be used with infrared light to avoid detection of the beam by the
wary or curious, and the cell has sufficient infrared response to permit the tungsten light
to be concealed by filters which transmit only this region with very little visibility of the
interrupted beam. The cesium-antimony cathode is rinding increasing application. Its
high efficiency to tungsten light makes it competitive with cesium oxide and considerably
superior with bluer modern illuminants. For colorimetric applications, a surface such as
the S3 is more suitable because of its broad spectral response through the visible region
which more nearly simulates the eye.
The requirements of precision photometry vary greatly according to the intensity and
color of the light to be measured and according to whether the measurements are relative
or in visual units. For example, in stellar photometry where very little light is available
and high amplification is necessary, leakage in and around the cell must be reduced to the
minimum and high sensitivity and color response may not be as important. On the other
hand, in the ordinary routine photometry of tungsten light, leakage may be relatively
unimportant. In precision photometry it is essential that cells be used in a manner which
gives an assured calibration for each reading and that their constancy be not assumed
without adequate proof. Cells to be used for measurements in visibility units require
either a filter to modify their color response or a calibration by a source whose spectral
emission is the same as that to be measured. If sources such as tungsten lamps through a
moderate range of color temperature are to be measured, requirements of commercial
photometry may be met by calibrating with a similar source within the range, combined
if necessary with a visual filter that approximately matches the eye.
The increasing use of ultraviolet for therapeutic and photochemical purposes has created
a demand for cells to measure intensities in this region, the response for therapeutic pur-
poses being of such shape as to evaluate the radiation directly in erythema units or in
time of exposure. This region is from 2SOO to 3200 angstroms approximately, the shorter
wavelengths of questionable value being excluded by filtering the source. A number of
materials are intrinsically sensitive to this region, but it is undesirable to use those of
considerable visible sensitivity because of the difficulty of suppressing sufficiently the
larger amount of energy in the longer wavelengths even in the mercury arc, which would
mask the ultraviolet response. Consequently it is desirable to use only those materials
which are not naturally sensitive much beyond 3200 angstroms. Cadmium, uranium, and
lithium have been proposed, and the first two have been used practically. In order to
limit the response to the proper wavelength on the short-wavelength side, these metals
can be mounted in bulbs of Corex D glass instead of quartz. If, for other purposes, it is
desired to broaden the region of response up toward or into the visible blue, thorium and
cerium have been suggested.
The glass bulbs of ordinary commercial cells are more or less opaque to radiation beyond
about 3200 angstroms, so that, hi any event, a special glass or quartz is necessary. The
cesium oxide cathode, however, is very sensitive to the longer ultraviolet up to 2000 ang-
stroms as far as measurements are available.
For certain purposes where an external battery is undesirable, cells of the barrier type
are finding application, an example being as a photographic exposure meter. It is neces-
sary, of course, to interpret the readings in terms of exposures for the various color sensi-
tivities of emulsions by charts or suitable scales on the meter.
Table 3 lists the better-known commercial cells.
BIBLIOGRAPHY
Gudden, LichfeleMri&che ErscJieinungen, Julius Springer, Berlin, 192ST
CiTnpbell and Ritchie, Photoelectric Cells, Sir Isaac Pitman and Sons, 1929.
Sinaon and Stihrman, Lichtelektrische Zellen, Julius Springer, Berlin, 1932.
Fleischer and Teiehman, Die lichtelektrische Zelle, Theodor Steinkopff, Dresden and Leipzig, 1932.
Hughes and DuBridge, Photoelectric Phenomena, McGraw-Hill Book Co. 1932.
Barnard, The Selenium Cell, Richard R. Smith, New York, 1930.
Deutsch-
Zworykin and Wilson, Photocells and Their Applications, John Wiley <fe Sons, 1932
Doty, Selenium, A List of References, 1817-19B5, New York Public Library, 1927.
Walker and Lance, Photoelectric Cell Applications, Pitman, London, 1933.
THE IMAGE DISSECTOR 15-19
Handbuch der Physik, Vol. XIX, pp. 829 ff. (Thermal cells.)
Koller, Physics of Electron Tubes, McGraw-Hill Book Co., New York and London, 1937.
Henney, Electron Tubes in Industry, McGraw-Hill Book Co., New York and London, 1937.
Reich, Theory and Applications of Electron Tubes. McGraw-Hill Book Co., New York and London, 1944.
' ~ ' "" - - - - ~ - - - 354 (June 1946)>
35S (June 1946).
Brattain and Becker, Thermistor Bolometers, J. Optical Soc. Am., Vol. 36, 6, p. 354 (June 1946).
Cashman, R. J., New Photoconductive Cells, /. Optical Soc. Am., Vol. 36, 6, p. ?~~ "
TELEVISION PICK-UP TUBES
By V. K. Zworykin and E. G. Ramberg
8. REQUIREMENTS
The purpose of the television pick-up tube is to convert an optical image of the scene
to be transmitted into an electrical signal descriptive of the light distribution in the image.
In. all the pick-up tubes here considered the signal is obtained by scanning in sequence a
rectangular image area along a fixed number (e.g., 525) of adjoining horizontal scanning
lines; with an ideal transmission system and viewing device the instantaneous signal output
of the pick-up tube determines the brightness of a particular picture element (i.e., a square
whose length and height are equal to the separation of two scanning lines) in the reproduced
image, scanned in synchronism with the transmitted image.
A satisfactory pick-up tube must be capable of furnishing a signal that can be converted
into an image with adequate detail, free from objectionable random fluctuations in bright-
ness (noise) , and faithful in geometry and tonal values over its entire area, at a reasonable
illumination of the transmitted scene. Similar requirements regarding resolution, signal-
to-noise ratio, uniformity, and sensitivity must also be fulfilled by the 35-mm negative
film employed in commercial motion-picture production, whose properties may reasonably
be taken as a standard. This is all the more appropriate since the comparison of television
with motion pictures appears inescapable.
SENSITIVITY. A suitable figure of merit for the sensitivity is given by the ratio
/Y (BA) , where /is the /-number of the lens employed, B the brightness of the scene required
to yield a good picture (in lumens per square meter) , and A the area of the picture on the
film (in square meters) ; through the factor f/A the figure of merit is proportional to the
square of the depth of focus. Employing figures derived from motion-picture studio
practice, / = 2, B = 5500 (lumens/m2), and A = 0.00032 m2 (0.5 in.*), J*/{BA) = 2.3.
RESOLUTION AND SIGNAL-TO-NOISE RATIO. Thirty-five-millimeter film is
generally capable of resolving 1000 to 1500 lines per picture height; on the other hand,
at this level the photographic grain or noise interferes seriously with the picture detail
(i.e., the signal). For a ratio of the signal to the root-mean-square noise amplitude of
30-40, required to render the grain unobjectionable, the resolution must be reduced to
about 500 lines. It should be noted that the root-mean-square noise amplitude employed
throughout in the present discussion is only about one-sixth as great as the peak-to-peak
noise amplitude, which may be observed directly on an oscilloscope screen. It is found
experimentally that the signal-to-noise ratio for film remains approximately constant
throughout the useful exposure range. It differs in this from the more sensitive television
pick-up tubes, for which the noise is constant and the signal-to-noise ratio, hence, is lower
in the low lights than in the high lights.
UNIFORMITY. The W™ image is geometrically faithful and uniform in response over
the entire image area.
It will be seen that certain pick-up tubes exhibit higher sensitivity and signal-to-noise
ratio for equal resolution than film. To this extent they enable television cameras to
function more favorably than studio and news motion-picture cameras.
9. THE IMAGE DISSECTOR
The Farnsworth image dissector is shown, in schematic cross-section, in Fig. 1. At one
end of the tube there is a photocathode on which a lens projects an optical image of the
scene; at the other, a positive electrode with a tiny aperture, equal to a picture element
in size. The magnetic field of a solenoid focuses the photoelectrons so as to form, in the
plane of the aperture, a charge image of the picture on the photocathode. This charge
image is swept across the aperture by the magnetic deflecting fields so that, at any instant,
photoelectrons from just one picture element on the photocathode pass through the
aperture. These accelerated photoelectrons fall on the first stage of an 11-stage multiplier
(see article 4) built into the tube and eject a larger number of secondary electrons which
15-20
ELECTRO-OPTICAL DEVICES
are drawn through, an accelerating screen to the second target electrode, leading to a
further secondary-emission multiplication of the current. The output of the multiplier,
finally, may be coupled by a resistance to the input of a standard video amplifier. _
.Magnetic focusing coll
"ZTEfeotron multiplier
..Nickef wall coating
Photo cathode
- Output lead
FIG. 1. The Image Dissector
The current passing through the aperture is simply the photocurrent emitted by a
picture element on the photocathode. Thus, if p is the photosensitivity of the cathode
in amperes per lumen, L its illumination in lux Gumen/m2), A the effective area of the
photocathode in square meters, and N the number of picture elements, the signal current
becomes
^Denoting the transmitted band width by F, the shot-noise amplitude for this current is
Assuming F = 5 - 106 sec"1 and a 525-line picture (2V = (525)2 - 4/3),
^2x2 — 2.1 •
Hence the signal-to-noise ratio is
c jf I * *yz i o
w — tg' Trn — I .o
If it is assumed that p = 20 * 10 ~* amp/lumen, A — 0.01 m2 (15 in.2)
(3)
(4)
(5)
A signal-to-noise ratio of 100 would thus demand a cathode illumination L = 29,000 lux.
The multiplication provided by the multiplier should be such that the multiplied shot
noise exceeds the amplifier input tube noise current, which may be estimated at 2 • 10 ~9
amp. Since
i^ - 1.6 - 10-»S (6)
the multiplier gain will suffice for all recognizable picture detail (S > 1) if it is equal to a
few thousand. The actual gain is made larger than, this, reducing the required amplifier gain.
SENSITIVITY. From the above figures it follows that, in order to transmit a picture
with a signal-to-noise ratio of 100, an image dissector provided with an //4.5 lens would
require (for an effective cathode area of 0.01 m2) a high-light brightness of the scene equal
to 29,000 (2-4.S)2 = 2.3 -106 lumens/m2. The figure of merit of the dissector, calculated
in the same manner as for
D'fssector
film, hence becomes
4.52 1
0.01 -2.3- 105 ~ 1100
(7)
FIG. 2. Motion Picture Transmission with Image Dissector
Thus the sensitivity of the
dissector is less than that of
film by a factor of two or
three thousand. This is a
drawback for direct pick-up
but is of secondary import-
ance for motion-picture
2).
For the latter purpose, continuously moving film is generally employed
Ttie film motion provides the vertical deflection, so that only the horizontal
coil need be actuated. Special types of image dissectors, designed spe<jifically
THE ICONOSCOPE
15-21
for the transmission of black and white and of color film, are available. Since the standard
projection speed for motion pictures is 24 frames per second and the television field
frequency is 60 per second, the arrangement shown in Fig. 2 is generally modified by
the insertion of an optical compensation system between the continuously moving film
and the dissector tube. This causes the motion-picture frames to be scanned two and
three times in alternation.
RESOLUTION. Under normal circumstances the aperture size determines the resolu-
tion of the image dissector. Change of focus with deflection is readily compensated by
applying the proper correcting signals to the focusing current or the accelerating voltage
in synchronism with the deflection. Fundamentally, the resolution of this type of tube
is limited by the unsharpness of focus arising from the initial velocities of the photo-
electrons. An increase in the number of picture elements demands, hence, either the em-
ployment of a larger photocathode, leaving the length of the tube unaltered, or a higher
operating voltage and stronger focusing field.
SIGNAL-TO-NOISE RATIO. The signal-to-noise ratio of the image dissector is pro-
portional to the square root of the scene brightness. Hence, for equal signal-to-noise ratio
in the high lights, the noise will be more prominent in the low lights than for film, though
less prominent than for most of the remaining pick-up tubes to be considered, for which the
noise is independent of the light level. It is therefore necessary to demand a higher signal-
to-noise ratio in the high lights than for film (e.g., 100 in place of 30-40). The fact that
the noise becomes more noticeable in the low lights is accentuated by the circumstance
that the signal output of the dissector is strictly proportional to the element brightness,
i.e., that the tonal scale is not compressed by the pick-up device.
UNIFORMITY. The image dissector has excellent uniformity properties, both with
regard to constancy of response over the entire picture and to the absence of geometric
distortions.
10. THE ICONOSCOPE
The iconoscope, the orthicon, and the image orthicon may be classed together as storage
pick-up tubes. In all of them the charge released photoelectrically from a picture element
by the incident light is stored in the period intervening between two successive scannings
of the element. This leads to a very great gain in sensitivity in comparison with non-
storage pick-up systems such as the image dissector.
Figure 3 shows the construction of a standard iconoscope (type 1850-A) with magnetic
deflection. It is seen to consist of an electron gun whose beam is deflected across the
surface of a photosensitive
"mosaic" by two pairs of Mosaic
external deflecting coils, and
the mosaic, all enclosed in
a dipper-shaped envelope.
An image of the scene to
be transmitted is projected
by a lens through an opti-
cally clear face of the enve-
lope onto the mosaic plate
whose dimensions are 4 3/4
X 3 9/i6 in.2
A typical gun structure
consists of an indirectly
heated cathode enclosed in
a grid cylinder with a 0.040-
in. aperture, a closely spaced
cylindrical accelerating elec-
trode at full anode voltage
with a denning aperture 0.002 in. in diameter, a focusing electrode or first anode, and
the final anode in the form of a platinum coating on the inner wall of the gun tube.
The defining aperture, which coincides approximately with the cross-over, is imaged by the
equipotential electron lens formed by the two cylinders at full anode potential and the
intermediate focusing electrode on the mosaic, forming a spot 0.005 in. or less in diameter;
this design minimizes the current striking the focusing electrode or first anode and hence
prevents disturbing secondary emission from the gun. In practice the anode is maintained
at approximately 1000 volts, the focusing electrode at 300 volts, and the grid bias may be
varied from — 30 to — 50 volts. The optimum Iconoscope beam current ranges from 0.05
to 0.2 microampere, increasing with the illumination of the mosaic.
v ^-~
Magnetic deflection
Focusing electrode
~ (1st anode)
Grid
PreampiJEei
The Iconoscope
15-22
ELECTRO-OPTICAL DEVICES
100
The mosaic is a thin sheet of mica, covered, on the side facing the lens and the electron
beam, with an array of minute silver globules, small compared with a picture element.
These have been rendered photosensitive by a process involving oxidation, cesiation, and
the subsequent evaporation of silver. On the other side the mica sheet is coated with a
continuous metal film, the signal plate, which
is electrically connected to the coupling re-
sistor and the grid of the first stage of ampli-
fication. The capacitance between the signal
plate and the photosensitive mosaic is of the
order of 1 pcf/m2; the total capacitance be-
tween signal plate and anode coating, 10 /t/zf.
The photosensitivity of the mosaic is 4-10 jua/
lumen; its spectral response is shown in Fig.
4. For a mosaic illumination of 10 to 50 lux
a coupling resistance of 0.1 megohm is recom-
mended. At very low light levels (and a
beam current of the order of 0.05 ju&) it is
proper to increase this to 1 megohm.
Figure 5 shows a smaller Iconoscope (type
5527) , with electrostatic deflection and trans-
parent signal plate, which is designed pri-
marily for industrial and amateur use. It
has a 1.4-in. mosaic and operates with a
beam voltage of 800 volts and a first-anode
voltage between 125 and 250 volts. The
cut-off voltage for the control grid is about
— 75 volts, and the horizontal and vertical
deflection voltages are in the neighborhood of
100 volts.
3000
4OOO 5000 6000
Wavelength, angstroms
7000
FIG. 4. Spectral Response of the Type 1850-A
Iconoscope
OPERATION, Superficially, the operation of the Iconoscope may be described as
follows: The mosaic functions as an array of minute photoelectric cells with a common
anode, whose cathodes are capacitatively coupled to the signal plate. The elementary
condensers so formed charge up, as the mosaic is exposed to light, by an amount propor-
tional to the light intensity. Whenever the beam, acting as a commutator, sweeps across
them, the cathode elements are returned to their equilibrium potential by collecting the
requisite number of electrons from the beam, and an equal electron current passes through
plates
FIG. 5. Small Iconoscope with Electrostatic Deflection (Type 5527)
the signal lead. For an illuminated element on a generally dark mosaic (for which the
total photocurrent would be very small), the signal current would be given by
AT
'J TT = PLA
(S)
employing the following notation:
p photosensitivity of mosaic.
L luminous flux/unit area of mosaic.
.4 area of mosaic.
N number of picture elements.
T frame time.
*e time required to sweep over one picture
element.
This would represent a gain in sensitivity relative to non-storage devices (without second-
ary-emission multiplication of the signal) which is equal to the number of picture elements.
The above representation is greatly oversimplified. Thus, it assumes that a mosaic
soanped in darkness has a uniform potential. The actual, measured, potential distribution,
at the moment when the scanning beam is approximately a third from the top of the
THE ICONOSCOPE
15-23
-t-
Top of mosaic
mosaic, is as represented in Fig. 6. Figure 7 shows the variation of the potential of a
particular illuminated and unilluminated element in the course of a frame time. This
behavior arises in the following manner. Considering the unilluminated mosaic, an element
directly under the beam emits secondary electrons whose initial kinetic energy varies from
zero to a few electron volts. The secondary-emission properties of the mosaic are such
that, on the average, about 4 secondary electrons are emitted for every primary electron
incident from the beam. These will be able to leave the element only if the field conditions
in front of it are favorable; as the element becomes, as the result of secondary emission,
more positive with respect to the anode and the remainder of the mosaic, a larger propor-
tion of the electrons will return to the element. When the element reaches a potential V\
of the order of 3 volts positive with respect to the
anode coating, only one secondary electron will leave
the element for every incident beam electron and no
further charging will take place. The beam current
is chosen large enough to bring the picture element
to the equilibrium potential Vi in every transit.
Since the mosaic is insulated, on the average only
one of all the secondary electrons (and photoelectrons)
which leave the element for every incident beam elec-
tron arrives at the second anode; the rest are redis-
tributed over the remainder of the mosaic. This re-
distribution is influenced by the potential distribution
over the mosaic (and hence, for an illuminated mosaic,
also, to some extent, by the light distribution in the
image) and the geometry of the tube — in particular
the location of clear glass surfaces relative to the
mosaic. The redistribution quickly reduces the po-
tential of the elements immediately behind the beam
and more gradually that of the more remote elements,
-KL +2
OB
j!
+3
Volts
Bottom of mosaic
FIG. 6. Voltage Variation over Icono-
scope Mosaic Scanned in Darkness
When the&elements have attained a potential Vz, of the order of - 1 1/2 volts, no further
redistributed electrons reach them. This, thus, represents the equilibrium potential of
elements not under the beam.
Consider, next, an illuminated element of the mosaic. Immediately after the beam has
rendered the element about 3 volts positive with respect to the second anode, no photo-
electrons are able to reach the second anode; however, an appreciable number may find
their way to the elements ahead of it which have been under the beam even more recently
and hence are more positive. Thus the element becomes negative less rapidly than an
unilluminated element. However, the photoemission is far from saturated, a large propor-
tion of the photocurrent returning to the element of origin. Although a larger proportion
of the photocurrent will reach the anode as the element becomes more negative, the condi-
tion of incomplete saturation generally persists practically up to the succeeding ^passage
of the scanning beam, at which point the illuminated element may have a potential PS, a
fraction of a volt above F2. At low light levels the average photocurrent leaving a small
illuminated region, with the rest of
the mosaic ha darkness, is approxi-
mately 20 per cent of the saturated
photoemission.
As the beam passes over the illu-
minated element, it returns it to the
positive equilibrium potential "Fi.
For a small illuminated area on a,
dark background, the signal current
is equal to the difference in the frac-
tion of the secondary-emission cur-
FIG. 7. Voltage Variation of an Uliiminated and an
illuminated Picture Element on the Iconoscope Mosaic
rent from the element which reaches the anode for the illuminated and for an unillumi-
nated region. This is simply the current reaching the anode as an uniBuminated element
is raised, under the beam, from the potential F2 to the potential F3 (see Fig. 7). Since
for both these potentials the secondary emission is, in general, saturated, and the current
collected by the anode must equal the beam current, only a fourth of the stored charge
can be utilized for the signal current if the secondary-emission ratio is 4. Thus the total
operating efficiency at low light levels is of the order of 5 per cent (1/4 of 20 per cent),
and the signal current is given by
i, = kpLA k ^ 0.05 (9)
It may be noted that the photoelectric efficiency can be improved appreciably by iHuml-
15-24
ELECTRO-OPTICAL DEVICES
nating slightly the photosensitive clear glass walls of the tube (backlighting), since this
raises their potential.
At high light values the efficiency becomes much less; regardless of the degree of illumi-
nation, photoemission will drive an illuminated region only positive enough relative to
its surroundings to prevent the departure of additional photoelectrons. Thus the Icono-
scope signal is compressed in the high lights. The preferred collection of the redistributed
electrons by the more positive areas of the mosaic enhances this effect. At very high light
levels the Iconoscope signal is determined by the photoelectric charge stored during the
line scan of the beam preceding the scanning of the picture element considered: Since under
the beam an element becomes positive by 3 volts relative to the second anode, the photo-
emission of the neighboring element on
the Line ahead of the scanned line is
saturated even if it is positive by sev-
eral volts relative to its other neigh-
bors ("line sensitivity") ; an opposing
voltage of 1-2 volts suffices to suppress
the photoemission.
The signal output characteristic of
the 1850-A Iconoscope is shown in
Fig. 8.
SIGNAL-TO-NOISE RATIO. The
principal source of noise in the conven-
tional Iconoscope pick-up system is
the noise introduced by the input tube
of the signal amplifier, which may be
represented as thermal noise from an
equivalent resistor TT added to the re-
sistive component of the coupling net-
work between the Iconoscope and the
amplifier. Since, for coupling resist-
ances of the order of 0.1 to 1 megohm,
the coupling impedance is primarily
capacitative for the high frequencies
of the video band (the combined ca-
pacitance to ground of the signal plate
and the grid of the input tube may be of the order of 15 pid, corresponding to about
2000 ohrns at 5 megacycles), it is necessary to insert a peaking network in the amplifier
to equalize response at low and high frequencies. This network causes the noise spectrum
to be concentrated in the high frequencies. For low-noise input tubes and a video band
of 5 megacycles, the ratio of the signal to the amplitude of the integrated noise may be
calculated to be
S = 5-108i« (10)
4 being measured in amperes. It should be noted that about 2 or 3 times as much of this
peaked noise can be tolerated by the observer as shot noise (e.g., from a multiplier) dis-
tributed uniformly over the spectrum.
SENSITIVITY. In practice a scene brightness from 6000 to 17,000 lumen/ma is found
to give satisfactory pictures with an 1850-A Iconoscope used in conjunction with a lens
of //5.6 or smaller aperture. The target area of the mosaic is approximately 0.011 m2
(17 in.2). Employing the lowest values both for the illiiminati.on and the /-number, the
figure of merit used as a measure of the sensitivity becomes
microamperes
0 0 C
M to i
Ol O C
/
"""
/
'
/
/
Signal output
p p
to 01 o
/
/
'
5 7 10 2O 30 40 50 70 100 20
Highlight illumination of mosaic, lux
FIG. 8. SIgnal-versus-Light Characteristic of Tyi
1850-A Iconoscope
5.62
6000-0.011
0.48
(11)
This is about J/5 that for film; the formula for the signal-to-noise ratio yields a value of
100, in harmony with direct measurements. This is greater than for filrr> by a factor be-
tween 2 and 3. Such a factor is needed to render the noise unobjectionable in the low
lights, since the noise does not decrease in proportion with the signal. The fact that the
signal output of the Iconoscope has less contrast than the original image, i.e.,
1 AT.
7 — where k - 2 — 3
k L
(12)
a condition which is generally compensated in the viewing tube, leads to a useful reduction
ia the difference between the signal-to-noise ratios for the high lights and the low lights.
RESOLUTION. The resolution of the Iconoscope, as for the other pick-up tubes here
eomsidered, may be extended to better than 1000 lines; for the 5254ine standard it is
THE MONOSCOFE
15-25
customary to peak the high-frequency response electrically so as to keep the response level
up to 500 lines.
UNIFORMITY. The description of the operation given above makes it evident that
the signal output for any picture element is not simply related to its brightness; the re-
distribution of the secondary and photoelectrons makes it dependent both on the geo-
metrical position of the element and on the light distribution in the remainder of the
picture. Hence spurious signals — "shading" — are introduced and must be compensated
electrically with the aid of shading controls. They become particularly troublesome when
large dark areas are present in the scene.
11. THE MONOSCOPE
The monoscope is not, strictly speaking, a pick-up tube. It merely serves to supply &
standard picture signal, whose character is prescribed by the preparation of the target
electrode. As such it has found
application primarily in the
testing and aligning of the com-
ponents of a television system
other than the pick-up tube it-
self.
Figure 9 shows the construc-
tion of a type 2F21 monoscope.
It consists of an Iconoscope gun
and a target plate (3 Vie by
2 5/ie in.), normal to the axis of
the gun, mounted in a pear-
shaped envelope. The target
Pattern electrode
FIG. 9. The Monoscope
plate consists of sheet aluminum on which a pattern has been printed with a carbon ink
(Fig. 10). The magnetic beam deflection and the circuit connections are the same as for
an Iconoscope, with the distinction that the anode coating is maintained at a potential
50-200 volts positive with respect to the target plate.
FIG. 10. Pattern on the Type 2F2I Monoscope
The operation of the monoscope depends on the much greater secondary emission ratio
of the slightly oxidized aluminum (~3) as compared with that of carbon ( <1). Whenever
15-26
ELECTKO-OPTICAL DEVICES
the beam strikes the aluminum, a signal current approximately twice as great as the beam
current flows through the signal lead in such a direction as to make the grid of the input
tube positive; when it strikes the carbon, a small current in the opposite direction tends
to make it negative. If a monoscope replaces an Iconoscope without changes in the ampli-
fier, the portions of the pattern printed in carbon ink will appear bright in the final image.
Dark and light may, of course, be interchanged by adding or subtracting one stage in the
video amplifier. A peak-to-peak signal amplitude of several microamperes may be ob-
tained with this tube.
12. THE ORTHICON
The primary defects of the Iconoscope, namely, shading and low efficiency of operation,
both arise from the redistribution of secondary electrons and photoelectrons on the
mosaic. This, in turn, is a consequence of the fact that the equilibrium potential of the
mosaic under the beam is close to anode potential, in fact, slightly positive with respect
to it. If, however, the beam arriving at the mosaic has, initially, a kinetic energy of 10
electron volts or less, the secondary emission ratio is less than unity and the potential of
the mosaic will drop to a value slightly below that of the emitting cathode; at this equi-
librium potential no additional electrons can reach the mosaic. Instead, the beam elec-
trons reverse their direction at a point close to the mosaic and are collected by some
electrode at positive potential. Portions of the mosaic which are in complete darkness
remain continuously at the equilibrium potential and, hence, give rise to no signal current.
Illuminated areas, on the other hand, lose electrons, between successive scannings, in exact
proportion to the quantity of light incident on them. The low-velocity beam, as it sweeps
over such areas, supplies just enough electrons to the mosaic to neutralize the stored charge
and causes the passage of an equal signal current through the signal lead. In brief, the
actual operation of such a low-velocity Iconoscope fits perfectly the original, oversimplified
version given for the operation of the Iconoscope.
The practical realization of the low-velocity Iconoscope demands fulfilment of two
conditions: (1) in order that the equilibrium potential (and scanning spot) may be uniform
over the mosaic, the beam must be perpendicular to the mosaic at all points; (2) to keep
the effective spot size small, the lateral velocity components of the electrons must be kept
small. These requirements are met by the special methods of beam deflection and focusing
incorporated in the orthicon.
The envelope of a typical orthicon (Fig. 11) is a 4-in.-diameter tube 14 in. long with a
short neck for the gun at one end and a flat, clear window for the transmission of the
Focusing Anode
coll dfsk
FIG. 11. Orthicon with Electrostatic Horizontal Deflection
optical image at the other. It is inserted in a long solenoid providing a uniform longitudinal
magnetic field of 0.007 weber/m2. The envelope contains, in addition to the gun, a pair
of curved electrostatic deflection plates which occupy half of the tube nearest the gun, and
a mosaic with a translucent signal plate having a target area 2 5/16 by 1 3/4 in. The hori-
zontal deflection is accomplished with the aid of the electrostatic deflection plates; the
vertical deflection, by a pair of coils mounted over a portion of the second half of the 4-in.
cylinder.
The principal peculiarities of the deflection and focusing properties of the orthicon are a
consequence of the presence of the longitudinal magnetic focusing field. In particular,
near the mosaic, where the magnetic field lines are perpendicular throughout to the mosaic
surface, the field assures the normal incidence of the electron beam: In a strong magnetic
Mid tlhe electrons spiral about the magnetic field lines.
Proceeding from one end of the tube to the other, the electrons leaving an indirectly
THE IMAGE ORTHICON 15-27
heated cathode through an aperture in the grid cylinder (cut-off voltage, -40 volts) are
accelerated through an aperture at 225 volts and restricted to a narrow pencil by a defining
aperture 0.0025 in. in diameter which is electrically connected to the accelerating aperture.
This pencil, the scanning beam, is focused by the longitudinal field, which is strong enough
to form a succession of images of the denning aperture less than 2 in. apart. Its current is
generally of the order of 0.3 microampere, i.e., just enough to discharge the most strongly
illuminated portions of the mosaic. After passing through another larger aperture in the
anode disk (at 250 volts), which separates the gun chamber from the deflection chamber,
the electrons enter the electrostatic deflecting field between flared plates. The simultane-
ous action of the electrostatic field and the longitudinal magnetic field causes a lateral
displacement of the beam parallel to the plates and proportional to the deflection voltage
(160 volts, peak to peak). The faring, making the increase and decline of the deflecting
field gradual, prevents the development of cycloidal loops in the crossed fields and, hence,
the acquisition of considerable lateral velocity components by the beam electrons.
Next, the beam passes through the magnetic deflecting field (0.0025 weber/m2, peak to
peak) which simply warps the field lines, so that the beam experiences a second displace-
ment, in the direction of the deflecting field (not at right angles thereto). After leaving this
deflecting field the electrons pass through a decelerating ring electrode at 100 volts (desig-
nated as "rotator electrode/* since the simultaneous action of the lateral components of
the decelerating field and the longitudinal magnetic field causes a slight rotation of the
scanning pattern) painted on the envelope to the mosaic, which is inserted in a mask
maintained 3 volts negative with respect to the cathode. Both the signal plate and the
photosensitive mosaic are translucent. Although the requirement of translucence reduces
the photoemission of the mosaic, as compared with that of the Iconoscope, this is more
than compensated by the greater efficiency of operation.
SENSITIVITY. It is found in practice that a studio scene with a brightness of 700
lumens/m2T transmitted with an f/2 lens, will yield a picture with a signal-to-noise ratio
of 1 00. The target area being 0.0026 m2 (4 in.2) , the figure of merit, of the orthicon becomes
700-0.0026
2.2 (13)
This is the same as the figure for film and better by a factor of 5 than that for the Icono-
scope. However, since the orthicon does not compress the brightness scale in the same
manner as the Iconoscope, but has a strictly linear response throughout, a signal-to-noise
ratio higher by a factor of 2 or 3 may be required in. the transmission of naturally contrasty
outdoor scenes to attain an equal freedom from noise in the low lights. Hence, under
such circumstances a more appropriate value for the figure of merit is 1.
SIGNAL-TO-NOISE RATIO AND RESOLUTION. A signal-to-noise ratio of 100 is
readily obtained. Attempts to exceed this value by increasing the brightness of the light
image frequently result in a loss of resolution and a local distortion of the scanning pattern
at the boundaries between bright and dark areas.
UNIFORMITY. If the image brightness is kept within the normal operating range the
signal output yields a faithful representation of the geometry and tonal values of the scene.
Scene details of excessive brightness (e.g., the explosion of flash bulbs) may, however,
cause a portion of the scene to be blacked out. At such points the photoemission charges
the mosaic up to a positive potential at which the secondary-emission ratio of the beam
electrons exceeds unity, so that the beam renders the illuminated area more positive instead
of discharging it. After the cause has been removed, normal operating conditions are
gradually re-established by surface leakage.
13. THE IMAGE ORTHICON
In the image orthicon a very great gain in sensitivity has been combined with the
freedom from spurious signals at low light levels which is characteristic of the orthicon
and the stability of operation at high light levels characteristic of the Iconoscope at the
expense of greater complexity of construction and alignment. The principal features which
distinguish the image orthicon from the ordinary orthicon are (1) an electron-optical
imaging section, making possible the employment of a more sensitive, continuous, photo-
cathode and secondary-emission multiplication at the target; (2) a two-sided target,
permitting limitation of the target voltage to a value sufficiently low to insure stability
at all light levels by providing a separate collector on the side opposite to the scanned side;
and (3) a secondary-emission signal multiplier, for the return beam current, which renders
the signal output sufficiently large that the shot noise in the beam, rather than amplifier
noise, determines the noise content in the reproduced picture.
15-28
ELECTRO-OPTIC Air DEVICES
Rorizontaf
& vertical
Photocathode Target
\Acceteraior /Deceterato
.grid, /
Grid
No. 4
Alignment
'"Grid E'ectro*
-,-- ., , No. 2 8un
/ Grid and /
/ No. 3 { dynode / Fire-stage
Focusing
c,o]l
Image
section
FIG. 12. The Image Orthieon
Figure 12 shows, schematically, the construction of the type 2P23 image orthieon. The
tube has approximately the same length, but, with the exception of the short end section,
a much smaller diameter than the 1840 orthicon. As with the latter tube, a long focusing
solenoid must be provided which envelops all the tube except the gun and multiplier
portion at the right extremity. The light image is projected on the flat transparent photo-
cathode (maintained at —300 volts) at the left end of the tube, and the photoelectrons
released by the light are focused by the magnetic field through a very fine-mesh (500-1000
meshes per inch), high-transmission screen on the target. Since the secondary-emission
ratio of the glass target
screen for 300-volt elec-
trons is much greater than
unity, a positive charge
pattern corresponding to
| NO. 1 / multiplier the light distribution in
\f / / __ the scene is formed on the
target. The secondary
electrons are drawn to the
closely spaced target
screen, which is usually
maintained at a potential
slightly positive (e.g., at
-f-lvolt) withrespecttothe
scanning-beam cathode.
The target itself is a very thin disk of low-resistivity glass. Its properties are such that
in the course of a frame time potential differences between the two sides of the target
built up at the instant of scanning are neutralized by conduction while the transverse
leakage of stored charge between neighboring picture elements still remains negligible.
The gun of the image orthicon has the same general construction as that of the orthicon.
However, the defining aperture is formed in the final disk electrode, which is exposed to
the return beam. The beam deflection is magnetic throughout, since this causes the return
beam to travel practically the same path as the scanning beam in reverse direction, striking
finally the electrode containing the defining aperture. The return beam itself carries the
signal; when the smarming beam strikes a portion of the target which has been rendered
positive by secondary emission, electrons equal in number to those lost in the course of a
frame time by the element under consideration are abstracted from the beam, reducing,
correspondingly, the current in the return beam.
The return beam strikes the defining-aperture disk with an energy of the order of 200
electron volts and ejects from it secondary electrons which, persuaded by the lower
potential of the electrodes facing it and the higher potential of a second stage of a pin-
wheel multiplier structure surrounding the gun, spill over into the same emitting a
larger number of electrons, which are drawn to the next stage. The total gain of the 1500-
volt five-stage multiplier is from 200 to 500, which is adequate to raise the shot noise level
in the beam (tV^-10"6 amp) above the amplifier input tube noise current (2-10"9 amp,
both for a 5-megacycle band width). At very low lights the proper value of the beam
current may, under ideal circumstances, be as low as 10~"10 amp, leading to a useful multi-
plier gain of 200; for a high-light picture a gain of 20 would suffice.
SIGNAL VERSUS LIGHT CHARACTERISTICS. Figure 13 shows a typical variation
of the signal output of the image orthicon with the high-light illumination of the photo-
cathode. The photosensitivity of the
photocathode is of the order of 10 micro-
amperes per lumen.
In the low-light range the image orth-
ieon functions just as the orthicon, the
signal current being proportional to the
light signal. At the knee of the curve
the secondary-emission charges the tar-
get just to the potential of the target
screen; beyond this point the response
curve flattens out, since an increasing
number of secondary electrons are forced
to return to the emitting element. As
the target becomes sufficiently positive
to lose only as many electrons by sec-
£ J.V
£
T^TO
See
Him
Oe:fc
tfiha
tac
iHon
<s and
salanc
:'iunj
wh
ed
jstei
/
tes-
/
>tcaf sflgnaj oatpt
o
OM
/
/
2.
31 0.1
1
10 10
£? Hlghllgnt illumination on photoca'thode, lux
FIG. 13. Signal-versus-Light 'Characteristic of Type
2P23 Image Orthicon
ondary emission as it receives from the photocathode, the response curve becomes com-
pletely, flat. This does not mean, however, than no intensity differences are transmitted.
LUMINESCENT AND TENEBRESCENT MATEKIALS 15-29
Redistribution of secondary electrons near boundaries between areas of different in-
tensity of bombardment (different brightness) results in potential differences at such,
boundaries. Thus a bright spot on a less bright background is transmitted as a bright
spot with a dark halo on a bright background.
SENSITIVITY. It is found that an image orthicon provided with an //2 lens and
capable of transmitting a picture with a signal-to-noise ratio of 100 can do so if the scene
brightness is 20 lumens/in2. Since the target area is approximately O.QOOS m2 (1.2 in.*),
the figure of merit of the image orthicon becomes
92
= 250 (14)
20-0.0008
This is approximately 100 times as great as the figure for film and for the ordinary orthicon
and over 500 times as great as that for the Iconoscope. A factor of 5 in this gain must be
attributed to the increased photosensitivity of the photocathode and the secondary-
emission amplification at the target; the remainder, to the signal multiplication in the
multiplier. To maintain freedom from objectionable noise in the low lights of high-
contrast scenes, it may be necessary, just as with the orthicon, to increase the signal by a
factor of 2 or 3, reducing the figure of merit to unity. It may be noted that the sensitivity
of the tube is sufficient to transmit pictures with some entertainment value even at a scene
brightness of 0.2 lumen/m2, corresponding to the brightness of light objects in full moon-
light.
RESOLUTION. The resolution of the image orthicon may be limited by the electron-
optical imaging process, the target screen, transverse leakage on the glass target, and scan-
ning spot size, the last being influenced by the defining aperture, the angle of approach of
the beam to the target, the initial velocity distribution of the beam electrons, and the
potential of the scanned area. In practice it is possible to attain a resolution of 500 lines
as with the other tubes.
UNIFORMITY. In the low-light range (the sloping part of the curve in Fig. 13), the
signal output is a linear function of brightness. For higher light values the tonal scale is
compressed, and, ultimately, contrasts, rather than absolute light values, are transmitted
primarily. This condition does not detract materially, however, from the apparent
naturalness of most reproduced pictures. Geometric distortions are inappreciable, al-
though slight non-uniformities in the target and the presence of the target screen tend to
make the picture somewhat inferior to that transmitted by the other pick-up tubes de-
scribed.
14. FIELDS OF APPLICATION OF PICK-TJP TUBES
The characteristics of the several pick-up tubes here discussed mark out spheres of
application for which each is particularly suitable. Thus, the relatively insensitive image
dissector, with its freedom from signal distortion, may be employed for the transmission
of motion pictures, for which very high light levels can readily be provided. The standard
Iconoscope is well suited for both movie and studio work, where the light distribution can
be controlled so as to simplify the compensation of shading. Its smaller, 2-in. version is a
convenient television pick-up device for industrial and experimental purposes. Spot pick-
up, with the attendant unpredictable conditions of lighting, demands the employment of
the image orthicon which, in view of its greater complexity and somewhat inferior picture
quality, may under other circumstances be replaced advantageously by the less sensitive
tubes. It is to be hoped and expected that further development of the image orthieon, as
the most recent of the pick-up devices, will raise the level of its picture quality to that of
the older pick-up tubes.
LUMINESCENT AND TENEBRESCENT MATERIALS
By H. W. Leverenz
Luminescence is a production of light in excess of thermal radiation (see ref . 5 on p. 15-41) .
Thermal radiation is emitted by electrons, atoms, ions, and molecules oscillating or
rotating singly or in groups as occasioned by thermal agitation.
An ideal thermal radiator is the perfect ttack body, which has complete absorptivity at
all wavelengths; i.e., it has oscillators available at all frequencies. The monochromatic
emissive power, EVr of a perfect black body (in vacuum) at frequency v (in sec"1), is a
15-30
ELECTRO-OPTICAL DEVICES
ir
si
si
>s
H
EXCITATION SPECTRUM
• SILICATES (ALSO
PICAL OF TONCSTATf
tD BORATES)
A
/\
I
I
t
1
I
1
I
\
EMISSION SPECTRA
OF TYPICAL SILICATE
GftEEN LUMINESCENCE)
function of temperature, T (In degrees Kelvin), according to Planck's radiation law:
Ev = 4.63 X icr5V(e7lJ'>'*T - I)"1 watts/m2 (1)
where h = 6.624 X 10 ~34 joule-sec (Planck's constant).
8 = 2.71828* - - (base of Napierian logarithms).
k = 1.38 X IQ-^Joule/deg (Boltzmann's constant).
The peak wavelength, Xmax, of the broad emission band of black-body radiation varies
with absolute temperature according to Wien's displacement law:
Xmax = 2.897 X IQ^T'1 m (1 m = 105 microns (/t) = 1010 angstrom units (A)) (2)
The total emissive power, ET, Ma black body is proportional to the fourth power of the
absolute temperature according to the Stefan-Boltzmann law:
E*r - 5.67 X lO-8^4 watts/m2 (3)
At room temperature, «300 deg Kelvin, Xmas is in the far infrared at 9.7 microns, and ET
is only 459 watts/m2. It should be noted that the nature of the material plays no role
in eqs. (1), (2), and (3). Although thermal radiation is emitted by all materials at tem-
peratures greater than 0 deg Kelvin
such radiation does not become visible
until the temperature is raised above
about 1000 deg Kelvin, when incan-
descence is observed. A temperature
of the order of 6500 deg Kelvin is re-
quired to shift the peak wavelength,
Xmax of thermal radiation into the
visible region of the spectrum £4000 to
7000 1). Thus far, no solid material
has been developed to endure pro-
longed operation above 4000 deg Kel-
vin, and so most of the energy emitted
from solid incandescent materials lies
in the infrared and their efficiencies of
light production are generally less than
about 5 per cent.
Luminescence is occasioned, by ab-
sorbed photons, so-called undulatory
energy (e.g., ultraviolet, x-rays, 7-
rays), or corpuscular energy (e.g.,
cathode rays or a-particles) which ex-
cite electronic transitions directly
rather than through the intermediate
stage of thermal agitation of atoms
and ions. Luminescence emission is
usually in the form of spectral lines or
narrow bands superimposed on the
broad band of thermal radiation from
a material. The spectral distributions
and efficiencies of luminescent mate-
rials are determined largely by their
chemical compositions and, if the ma-
terials are solids, by their crystalline
structures. The characteristic mono-
chromatic spectra of attenuated gases
4ZitO-6BtO'3SiOx:Mn
(YELLOW-ORANGE •
LUMINESCENCE)
3000
ULTRAVfOLET-
5000 6000
- VISIBLE
XX) 7000A*
EMISSION SPECTRA
OF TYPICAL SULPHIDE
r, PHOSPHORS
200O
PIG. 1.
j5
Excitation and Emission Spectra of Some
Typical Phosphors
are relatively simple luminescences whose efficiencies may approach 100 per cent for the
case of resonance radiation (Xexcltation = Demission)- In liquids and solids, however, the
perturbations imposed by near neighbors of a luminescing atom or ion complicate the
mechanism and generally lower the efficiency of luminescence.
The generic term luminescence is commonly modified by a prefix indicative of the
excitant used to cause luminescence. For example, photoluminescence is luminescence
excited by photons, and cathodoluminescence is luminescence excited by cathode rays. A
further distinction is made with respect to duration of luminescence after cessation of
excitation; i.e.t fluorescence lasts less than about 10~8 second whereas ^phosphorescence lasts
longer than about 10 ~8 second. The value of 10 ~8 second is the approximate lifetime of
eaceited non-metastable isolated atoms or ions and serves as an arbitrary demarkation
between fluorescence and phosphorescence. Materials, such as gases, liquids, organic
materials, and many glasses which exhibit fluorescence are called flitors; while phosphores-
LUMINESCENT AND TENEBRESCENT MATERIALS 15-31
CURVE
PHOSPHOR
CRYSTALLIZATION
TEMPERATURE *C
EXCITATION
,
<x*-ZnS IO"*Ni
73O
3650
*»-Z«S 0.003% Aq
P*-ZnS 0.015 %Aq
a*-Z«S O.OO3%CM
950
1240
660
3660
3*50
36iO
/3*-Z«S O.OO31&OJ
\20Q
3650
j3*-Z«S O
1260
3650
1200
2537
{3 - Znj Si CU : I fc Mn
I55O-O
2537
ZnO:CZ«0
IOOO
365O
300 J
600
TEMPERATUPE
PHOSPHORESCENCE •
F- SHORT- PERSISTENCE PHOSPHOR
P = LONG - '* ii
FIG. 2. Photoluminescences of Some Phosphors as a Function of Temperature
cent materials, which are chiefly crystalline inorganic materials, are called phosphors.
Some typical excitation and emission spectra of phosphors are shown in Fig. 1; several
temperature-dependence curves of
phosphor photoluminescences are
shown in Fig. 2, and some typical
excitation and decay characteris-
tics of phosphors are indicated in
Fig. 3.
Phosphor light outputs may be I
modulated by three methods: &
1. Positive modulation of lumines- 5
cence is the normal increase of light «
output with increasing excitation ?
density at temperatures below the |
fairly critical temperature, Tc, above t
which the efficiency of luminescence °
sharply decreases. t
2. Negative modulation of lumi- |
nescence is accomplished by increas- £
ing the temperature of an excited '"
phosphor above Te and thereby de-
creasing the luminescence.
3. Positive modulation of incan-
descence is accomplished by further
raising the temperature of the phos- <
phor until incandescence supplants p^ ^
luminescence.
EXCITATION
INTERVAL ""
DECAY INTERVAL -
The Relationships of Luminescence, Fluorescence,
and Phosphoresceace
15-32
ELECTRO-OPTICAL DEVICES
The last two methods of modulation involve thermal inertia of matter as contrasted
with the purely electronic transitions in positive modulation of luminescence. Positive
modulation of luminescence is unique in allowing useful modulation up to frequencies of
the order of 107 cycles per second, the limit for any particular phosphor being inversely
proportional to its characteristic decay time (the time taken to decay to an arbitrary
percentage, e.g., 1 per cent, of the luminescence at the last instant of excitation).
Tenebrescence is any non-intrinsic absorption of light induced in a material. For
example, normally colorless potassium chloride, KC1, whose intrinsic absorption is in the
^ rt0 o ,,-r « ne .. T-7 M far ultraviolet (left side of Fig. 4), may
12.34 6.17 4.11 3.08 2.47 2£6 1.77 *V *
JOOO 2000 3000 4000 5000 6000 7000 A ^.^ J^ spectrum by irradia-
tion with cathode rays or x-rays (see
right side of Fig. 4). The induced dark-
ening (tenebrescence) may be bleached
by irradiating the darkened material
with light having wavelengths lying
within the induced absorption band.
Intrinsic and Induced (Tenebrescence) Absorp- The Bleaching is accelerated by heat.
Intrinsic
Induced
FIG. 4.
tion Bands of Potassium. Chloride
Tenebrescent materials become increas-
ingly difficult to bleach as the duration and intensity of the primary irradiations used to
induce tenebrescence are increased. The relatively unbleachable absorptions are similar
to those of pigments or dyes which convert absorbed photons into heat. Bleachable
tenebrescences are ascribed to temporary trapping of electrons; unbleachable tenebres-
cences apparently involve concomitant ionic displacements.
Tenebrescent materials, such as the crystalline halides of alkali or alkaline-earth metals,
are called scotophors.
15. PREPARATION AND NOTATION OF PHOSPHORS
Successful preparations of synthetic phosphors require highly specialized chemical and
physical operations wherein even the most skilled and careful workers sometimes have
difficulty in reproducing results. Phosphor ingredients must be purified to contain less
CURVE
PHOSPHOR
RELATIVE VISIBLE
EFFICIENCY
COLOR
;
a-Zi>»SiO4:Mn(STCO
tf-Z**&CV-Mn
100
60
GREEN (5230 A)
YELLOW (563O £)
3000
UUWS/tOLET
4OOO
VIOLET
WAVELENGTH -ANGSTROMS
* 5. Cathodolumlnescence Spectra of «- and ^-Z
with and without Manganese Activator
than about 10~* per cent of undesirable metallic-ion impurities (e.g., iron, nickel, and
eliromiiim), since as little as 10~* per cent of combined nickel in a zinc-cadmium-sulfide
pi*ospfeor lowers efficiency about 25 per cent. On the other hand, 10 ~* per cent of com-
bined silver in the foregoing pure phosphor increases efficiency 100 per cent. The final
step in preparing phosphors is crystallization, where the purified ingredients are
PREPARATION AND NOTATION OF PHOSPHORS 15-33
CURVE
PHOSPHOR
TEMP.
FOR
RELATIVE
VISUAL
RESPONSE
NATURAL
COLOR
COLOR OT
LUMINESCENCE
RELATIVE ENERGY RELATIVE VISUAL RESPONSE
. § 8 § 8 § o § 8
1
a
3
5
6
7
ZnS:O.O08%A9
940°
»8.5(la)
WHITE
LIGHT BLUE
ZnS(80) CdS(20)'O.OI%Ag
'•
2T.O
LIGHT
GREEN WHITE
VERY LIGHT
BLUE GREEN
ZnS(60)ClS(40): "
66.3
VERY
LIGHT GREEN
VERY LIGHT
CREAM GREEN
Z*S(50)CdS(50): •«
"
IO&OG-)
LJGHT YELLOW
LIGHT GREEN
YELLOW
Zr.S(-30)CdS(60): »
"
63.7
LIGHT
CREAM YELLOW
LIGHT
YELLOW ORANGE
ZnS(20)CdS{60): ••
• •
9.4(6a)
TAN ORANGE
LIGHT RED
0,5:0.02%*,
»
—
LIGHT
BROWN ORANGE
RED
1
/
IN
a
S^~
^
IEYE
[MAX.
^
*c
»
vioirr
5
BLUC
00
CBCCM
M
rtttow
00
OftAMCE
TO
KO
•00
1
I
f
/
\
'EYE
I MAX.
I
/
V
^\
I
/
fr
X/^
P"
\ >
^
u,
v '/
^
IVJ.x
\
&-
5000 600O
WAVELENGTH -ANCSTROM UNITS
PIG. 6. Cathodoluminescence Emission Spectra of Some Silver-activated Zinc-cadmium-sulfide
Phosphors. Upper curves are the relative visual response characteristics of Nos. 1, 4, and 6.
Violet
Bftfe
Green
Yeftow Orange
mixed in fused-silica or platinum crucibles and heated in electric resistance furnaces,
generally to temperatures be-
tween 600 and 1600 deg cent.
The resultant phosphors are
masses of tiny crystals ranging 400
from less than 0.01 to about 100
microns in diameter. Most phos-
jphor crystals average about 1 to
15 microns in diameter. Some
-iypical initial compositions and
t corresponding notations of the
resultant phosphors are given in
•Table 1.
The luminescence emission
: spectra* of phosphors are strongly
.influenced by changes in crystal-
Ilization and composition, as
. shown in Figs. 5, 6, and 7. Phos-
.phors such as P3, P4(Y), and
P7/2 belong to "families"
wherein gradual base-material
-variations enable one to produce
emission spectra which may be
- varied continuously from one end
«of the visible spectrum to the
* other. Other properties, such as
4500
5000 5500
Waffielengtb, angstrom unfts
6000
65OO
FIG. 7. Cathodoluminescenoe Emission Spectra of Zinc-sul-
fide Phosphors Prepared with (1) no added activator, (2) copper
activator, (3) silver activator, and (4) gold activator
15-34
ELECTRO-OPTICAL DEVICES
absorption spectrum, efficiency, and phosphorescence, are also considerably affected by
changes in the structures and compositions of phosphors.
Table 1. Approximate Compositions and Notations of Some Useful Phosphors
RMA
Code
Base Material
Ingredients,
grams
Activator
Salt, grains
Flux,
grams
Crystal-
lization
Temper-
ature,
deg cent
Phosphor Notation
PI
P2
P3
P4(Y)
P4(B)
P6(B)
Pll
P4(Y)
P5
P6(G)
P6(R>
P7/1
PI4/1
P7/2
P12
PI 4/2
P15
81 ZnO -f- 31 SiO2
IDOZnS
0.5 MnO
0.02CuCl2 +
0.04 AgCl t
0.4 MnO
0.002 to 0.02
AgCl
0.02 AgCl
1250
1250
1250
950
950
1000
950
950
1250
1250
1000
1200
1000
tf-Zn2SiO4:Mn
0*-ZnS:Ag t:Cu
8ZnO -BeO - SSiOa : Mn
a *-ZnS:Ag
ZnS(48)-CdS:Ag
CaW04:[W]
ZnS(60)-CdS:Ag
ZnS(38)-CdS:Ag
(3 *-ZnS:Ag
Zn?(86)-CdS:Cu
ZrJFo:Mn
ZnS(75)-CdS:Cu
ZnO:[Zn]
SrS : SrSe : Sm (Tb) : Eu (Ce )
6NaCl
65 ZnO 4- 2.5 BeO +
31 Si02
100 ZnS
2NaCl
2 NaCl
48 ZnS + 52 CdS
57 CaO 4- 232 WO3 . .
60 ZnS -f 40 CdS
0.02 AgCl
0.02 AgCl
0.02 AgCl
0.02 CuCl*
0.5 MnF2
0.01 CuCl2
(Heat in CO
1000°
0.03 SmCls (or
TbCla) 4-
0.03
Eu-2(SO4)3
(or CeCis)
2NaCl
2NaCl
4 NaCl +
2 BaCl2
2 NaCl
38 ZnS + 62 CdS . .
100 ZnS
86 ZnS 4- 14 CdS. .. .
103 ZnFa . . .
75 ZnS 4- 25 CdS
2 NaCl
or H2 at
C)
6 (CaF2 4-
SrS03)
100 ZnO ...
100 SrS (or SrS +
SrSe)
a * = cubic; # * = hexagonal.
f = optional. (B) = blue, (G) = green, (Y)
ions may also be added as nitrates.
yellow, (R) = red. The Ag and Cu activator
16. MECHANISMS OF PHOSPHORS
Energy transducfions during excitation and emission of phosphor luminescences have
the following chronological sequence:
— 03) ^internal fluorescence ~}~
-^primary = ^reflected + ^^absorbed + cJ^escaped
— ^i-Stransmltted to activator centers Hr (& — &i) •S'lieat
activator centers = ^2-^stored ~f" (&i — ^2) ^Internal fluorescence
phosphorescence + fa
orescence —
luminescence ~h (
(5 l
where a + b + c = 1; 1 > b > bi > h* > h$ > h: and -^escaped is the residual primary
energy which completely penetrates the phosphor crystals or which emerges from the
side of incidence owing to internal scattering.
Luminescence emission is occasioned when a bound electron in energy state E$ is excited
to a higher allowed energy state, #ex» and returns to the same or an intermediate, energy
level, E&ct, emitting the energy difference, AJ? = J5?ex — E&r,t, as a photon of light. The
relations between energy AJ? (in joules), frequency v (in cycles per second), and wave-
length X (in meters), of photons are given by:
AE = hv =
(9)
where c = 3 X 10s m/sec (speed of light in vacuum).
Some of the features of corpuscular excitation of phosphors, such as by cathode raysr
may be exemplified with the aid of Fig. S, which shows generalized sketches of the interiors
ol pbosphor crystals, including three major classes of crystal irregularities (faults). The
total penetraiionT a?fT of 10s to 106 volt cathode rays in a phosphor of density a (in grams
MECHANISMS OP PHOSPHORS
15-35
per cubic centimeter) is calculable from Ten-ill's equation:
4 X 10ncr
cm (To in volt si
(10)
The fraction W/WQ, representing the power dissipated up to distance x in the crystal, is
given by StinchfiekTs equation:
W / x
=r - 1 - -y( 1
WQ \ xt
Cfx/xt
Charged-partide
excitation
(11)
where 7 « 1 for x/xt < 0.5 (7 increasingly exceeds unity for x/'xt > 0.5) , and C' ~ 32.
Over 50 per cent of the cathode-ray power is dissipated in the first quarter of the total
penetration distance, and over 80 per cent is dissipated in the first half of the total pene-
tration distance.
A few phosphors, such as ZnO:[Zn], may be excited by cathode rays with energies as
low as 5 volts, but such low- voltage excitation is quite inefficient because the excitation
energy is expended in the distorted
surface layers of the phosphor crys-
tals and the ratio of secondary to
primary electrons is usually less
than unity at such low primary"
voltages. Conventional, unmetal-
lized cathode-ray-tube screens must
have secondary-emission ratios equal
to or greater than unity to main-
tain .a positive potential with re-
spect to the cathode. The efficient
range of primary voltages is above
about 1000 volts, and preferably
above 10,000 volts for phosphors
whose limiting potentials (voltage
above which the secondary-emission
ratio falls below unity) are above
10,000 volts or phosphor screens
which may be coated with an elec-
tron-pervious reflecting and conduct-
ing coating, such as a 1000-A-thick
layer of aluminum.
As indicated in Fig. 8, the initial
energy, eV& of the primary particle
II
I *', h"z
a = substitutions! fmpurrty
& "interstitial Impurity
O = omission defect
("quantum energy emitted-}- (heat dev.)
y< \heat developed
I escape energy 4- heat dev.
fn
f absorbed ^
"< In
is expended bitwise and indiscrimi- ^ JttwMp*tion\>f * P
nately to the crystal atoms and ions. Single Absorption of a Primary Photon
The sizes of the absorbed energy
bits average about 20 to 30 electron volts, as determined by the characteristic frequencies
of bound electrons in the crystal (1 electron volt = 1.6 X 1Q~19 joule = 1.6 X 10 ~^ erg).
The average absorbed energy bits are relatively independent of the nature of the inorganic
material and the initial energy of the primary particle. A high degree of crystallinity is
essential for efficient cathodoluminescence, since the indiscriminately absorbed energy
bits must be transmitted to the sparse population of activator (phosphorogen) centers
with the minimum of attenuation. Glassy structure, crystal faults, and undesirable
impurities lower luminescence efficiency by converting absorbed primary energy into heat
as indicated in eqs. (5) and (7). The efficiency loss (as heat) in eq. (8) is occasioned by
the absorptivity of the phosphor crystal for its own luminescence. The more efficient
cathodoluminescent materials require an average of over 30 electron volts of primary
cathode-ray energy per 1.5 to 3 electron volt quantum of emitted luminescence. Hence,
the efficiency of cathodoluminescent materials has thus far been less than about 10 per
cent.
In photon excitation of phosphors, the primary photon, hvo, seeks out a spot in the crystal
to expend itself completely, not bitwise. The absorption of a primary beam, containing
no photons per unit cross-sectional area, is a function of penetration distance, xt into the
phosphor, according to: _ _As . .
where the absorption coefficient A is strongly dependent on the frequency of the primary
photon and the characteristic allowed frequencies in the phosphor crystal. The char-
acteristic frequencies of bound electrons in the base materials comprising the bulk0of
phosphor crystals lie in the far ultraviolet (v > 15 X 1014 cycles per second, X < 2000 A)
15-36 ELECTRO-OPTICAL DEVICES
Excitation of phosphors by near-ultraviolet photons results in direct excitation of the
foreign activator centers, and there is no need for a high degree of crystallinity. Good
photoluminescence, but inefficient cathodoluminescence, is obtained from amorphous
materials such as organic dyes, inorganic glasses, and certain inorganic crystals such as
the alkaline-earth-sulfide phosphors which contain some glassy structure caused by the
residual non-volatile fluxes used in their preparation.
Photoluminescence efficiency is limited both by impurities and crystal faults, which
convert primary photons and internal luminescence photons into heat according to eqs.
(5), (7), and (8)r and by the energy deficit, A#:
- Emitted) ~
Efficient phosphors, excited by near-ultraviolet photons, have photolumin escence efficien-
cies of the order of 60 to SO per cent, with quantum efficiencies near unity. At very high
energies of primary photons (or particles) the production of secondary radiations intro-
duces added complications in the mechanisms of excitation of phosphors.
There are two major types of luminescence-active centers in phosphor cyrstals:
Stibstitutionally located activators are exemplified by manganese which replaces zinc,
especially in phosphor crystals where oxygen or fluorine dominate the anion structure (e.g.,
zinc silicate, and zinc fluoride). These phosphors afford predominantly simple initial
exponential (&~af) decays of light output, L, after excitation to a peak luminance, LQ, accord-
ing to:
L = LQQ-at (t in seconds) (14)
where the constant a has known values ranging from 106 for ZnO:[Zn] to 10 for
(Zn: Mg)F2.* Mn. Exponential decays are determined largely by the chemical composition
of the phosphor, being relatively unaffected by changes in crystal structure, in tempera-
ture, or in the type, duration, or intensity of excitation. The luminescence action is
apparently localized in the substitutionally located activator sites as a metastable-state
monomolecular process, without necessitating electron transport outside the immediate
sphere of influence of the substitutional activator center. The observed weak photo-
conductivities of some 8~af-decay phosphors are probably associated with their later-stage
low-intensity power-law-decay "tails" which are strongly affected by changes in crystal
structure, temperature, and excitation.
InterstitiaUy located activators are exemplified by copper or silver interspersed among
the regular lattice units in phosphors where sulfur and/or selenium dominate the anion
structure. These phosphors afford so-called power-law (t~n] decays represented by
where both 6 and n are not true constants but vary with changes in £0, t, crystal structure,
or temperature, and with the type and duration of excitation. For practical purposes,
0 < b < 10 ~3 and 0.2 < n < 3 for known phosphors. There is a definite correspondence
between the strong photoconductivities and phosphorescences of most £~n-decay phos-
phors, indicating electron transport between the remote centers of trapping and emission.
In these cases, monomoleeular activated release followed by bi- or polymolecular mech-
anisms afford the complex £""* decays.
The optimum activator concentrations and maximum allowable impurity concentra-
tions in e~~ct-decay phosphors are about a hundredfold greater than those in £~n-decay
phosphors. Since the cube root of 100 is about 5, this means that interstitially located
impurities are affected by other impurities five times as remote, as in the case of substitu-
tionally located impurities. Substitutionally located impurities are in regions of lower
potential energy and are better buffered by close coupling with the lattice forces.
The optimum number of active luminescence centers and/or electron traps is about 1017
per cubic centimeter in £~n-decay phosphors and about 1019 per cubic centimeter in 8~ at-
decay phosphors. From these data, and data on the penetrations and power densities of
common excitants, it is possible to calculate the maximum phosphorescences of phosphors
with given decays.
17. MECHANISMS OF SCOTOPHORS
Figure 9 shows a schematic section of a crystal of potassium chloride, KC1, indicating
several omission defects and an interstitial defect. The fraction / of omission defects is a
function of equilibrium temperature T (degrees Kelvin) according to
wfeare, for KC1, A « 104 and TF0 » 1.6 X 10~19 joule. At temperatures near the melting
SPECIFIC CHARACTERISTICS OF- USEFUL PHOSPHORS 15-37
point of KCI (1074 deg Kelvin), / becomes about 0.2, and many of the omission defects
are frozen-in when KC1 is evaporated and condensed, as in making P10 screens. There-
fore, a large number of the 3.2 X 1022 lattice sites per cubic centimeter in PlO-screen
crystals are empty, and half of these omission defects are absent chlorine ions (Cl~) whose
vacant positions may be occupied by electrons to form scotophor color centers (so-called
F-centers) as indicated in Fig. 9. The visible absorption band of tenebrescent KC1 (Fig. 4)
corresponds to absorption of light by F-centers, i.e., ejection of the trapped electrons.
The maximum concentration of F-centers in KC1 screens is about 101S F-centers per cubic
centimeter.
Tenebrescence is quantitatively expressed as contrast, C, defined by
c_ 1000. -i«> (inpercent) (17)
LQ
where I/o and Ld are the luminances of the undarkened and darkened areas, respectively,
when observed under light having wave- _ _ / _
lengths within the induced absorption band of O O*O O* P+O
the scotophor. -._ ,-_
The decay of tenebreseence, i.e., the bleach- U P U O (
ing of induced darkening, is a power-law rela- rv*rT
tion of the general type u ^
e = eo*-» as)
where C0 is the tenebrescence (contrast) at O* O~ O* tfj? O4 Q~ O+ O""
time t — 0 and n decreases from about 1.5 to ^_ /-v_ , s-\-*+ s~\- ^3. /~\- r*-J-
less than 0.1 with decreasing temperature or U ° (J O*Vj^O {J VT^J U
intensity of illumination and with increasing CR-beam electron,
degree of tenebrescence. The useful decay FIG. 9. Schematic Section of a Crystal of Po-
intervals (time between successive excita- tassima Chloride (KCI), showing the formation
tions) of the best known scotophor, KCI, of an F-center- ^S^^. " C1~r ""^
range between 1 and 60 seconds at tempera-
tures near 40 deg cent and illuminations of the order of 10,000 foot-candles of light from
incandescent lamps.
The sensitivity of cathodotenebrescent KCI is about 1/ioo that of efficient cathodo-
luminescent phosphors; i.e., perceptible tenebrescence requires about 100 times as much
cathode-ray excitation energy as is required to produce perceptible luminescence.
18. SPECIFIC CHARACTERISTICS OF USEFUL PHOSPHORS
AND SCOTOPHORS
Phosphors and scotophors may be considered as high-frequency transformers which can
transform a megavolt-wide range of invisible photon or particle energies into emission or
absorption of light in or near the 1.5-volt-wide visible region of the electromagnetic spec-
trum. The output frequencies of these materials are in the range from about 4 X 1014
to S X 1014 cycles per second (red to violet).
The chief commercial uses of phosphors are in electron discharge devices, such as fluores-
cent lamps and cathode-ray tubes for radar or television. Fluorescent lamps contain
mercury vaapor at a pressure of about 4 M, which, under electron excitation, emits invis-
ible 2537 A radiation which, in turn, excites visible luminescence in an internal phosphor
coating. White-emitting coatings for fluorescent lamps are made by mechanically mixing
blue-emitting magnesium tungstate and yellow-emitting manganese-activated zinc-
beryl Hum-silicate phosphors which afford quantum efficiencies of the order of 90 per cent
and overall efficiencies four times as great as most incandescent lamps.
Cathode-ray-tube screens comprise a much greater range and variety of materials than
those used in fluorescent lamps. Table 2 shows some approximofe general properties of the
more useful cathode-ray-tube screens, including all those presently coded by the Radio Man-
ufacturers Association (RM A) . The screens are arranged in the order of their approximate
persistences after excitation by 6-kv cathode rays at about 1 microampere per square
centimeter. The dark-trace screen at the right of Table 2 exhibits decelerated decay as
the excitation density is increased; the sulfide-type bright-trace phosphor screens exhibit
accelerated decays with increasing degree of excitation. By observing a tenebrescent
image at some time after excitation, it is possible to obtain greater relative contrast between
image traces than during the excitation interval. Conversely, the normal bright-trace
screens may be used as contrast or ratio compressors.
15-38
ELECTRO-OPTICAL DEVICES
pc
?.
rt
o
o
?
q
H
^o
Q
«
T
^
1
02
^
sO
1
o
I
5
t-<
33
c
P3
S
r-J
2
H
V
0
1
0
cs
§
B
g
K
o
s
£3
S3
en
*
g
o
n
m 1 g
g
£
_
0
^
i
—
S
^
S
«
2
2
!
O
g'E^
^^3
^
"4
n
0
0
cs
o
H
'«
0
~0
a
CM
J^rt
?lH
si
O
H
rSti g
s^u
«
6 m
E^
r*
„
«o ^_^
!*§
+!
g
£
L-
o
«
-2
'S
! 111
0
O
!
02
a
.2
if
?
CO
o
g
Q
•^i«
o
0
w
O
ii
••-* 03
^O ^2 *&£]•'?
,s
"^
o ^^
S'P
'S a P^? "S
>
I
i
p*
*o
I
!
^,
-i ^ ' *"
iZ
i the Persistence
vO
S
bC
t«*
K
i
0
2
0
T
o
j
CRT acreen
p.
i§i
0 <=
Eloctronio
1
O
•0
lonochi'ome or
color television,
<P4 - bL and
wh., P6 w colo
S -2 ^ c
5j
&
CO
j5
o
fe
OJ
^
bC
£
o
"o ^
tj
S
si
1
5
V"S«Z-* »
i
g
S
a
^
I
r
CRTscm
S
u
0
d
0
Electroni
s
NO
ffi
"H D.
3 °
-^ 2
1
s^
S*1
5
1
£
c
!
'So
^
S
S
£
0
m
<£)
S
cs
2
o
2
m.
02
I
I
|
o
T
o
|l
S
"S
S
!^
£j
^5
•o
M'S o
sg
OD
°
Q
IIS
05
4i
0
c
f 0
i2
S3
£H
*?
T:
oo
T
c-4
S
^
ro
£
o
1^2
"® >e*
fx,
O
PP
1
S
~
0
"
EH
I
—
1 ;
o
sO
rt ^
|I4
Cfl
5
0
^*
3 ^^
"G'0 a.
j
-§ ^2^
jg §vr\
i
i
f^
H
£
^2
Jc>
•
^
1
0
C
jf
5
^
g
o
CJ
1
f.
|S
J|
0
0
g
g
o
c
SD
i
fc
3
.§
0
."1
S
OS
Cj
>-!
It
§l
ll
0
*2
i
2 ^
"e
S
'S
o
3
O
1
s
i
rf
"EU
3.
61
l~
i^
o-
3
«
Q
Q^
a.
1
S
1
SPECIFIC CHARACTERISTICS OF USEFUL PHOSPHORS 15-39
1
1 fft*t
> >> ;
i
S
.2
3
-fa
t||
J2"3
2
1
Q
I
^
r
0
1
1
"s
i
u"*
5
c?
5
l!j
1lJ
2*g
s
t:
"H
c
0
£<2"il
•5 §•§
1
r3
1
i|1|
III
W
1-1
*""*
SB i
-= '£
go
£
g g—y
^
o
^
1
c
c,— ^* c
§
rs.
ft.
02 ^-s
PQ
White-yel
0
:
0
0
Q
t
Electron
u^
i
0
« 3 « a
Ililj
&
Is
«i{S3
J'ig'al
II
* 5?
f~*
d
93 £
.2
•-C "*
.a
;>
*o
a
^.
go
bcai
^H-O
-O
H
1
oi
?
_
r
C
ao icon
?
o
1
t
aj *x
'"'S o
MS a
J^\ t£
1
90
§
o
I
E
gin^
f-i
jB
s
CN
-
en
E-i
P?
~~*
1
0
•gl J
t>
'I
o
* CO
^N
1
0
O
11
^ CJ
PW
ryt
c^
C3
|
T3
5
Jf
fl
£5"*-
*C>r
S
C 53
Is
^
q
CJ
—
o
IK
1
f
m
1
e
I 53 8
|fr.
sf
P-i
ad
rt
s
o
"*"
1
0
v_*
35
T^
0
"o
!
.5*-"1 S.
^ a
o
d
O
—
^
•« J1" '
a: =S
g
*
o
O
K
l?l
•|S
."S
ill
J^3
~s
0)
-^
S
^
OQ
3
H
S
o
c
£
o
P
-&|
CM
1
S
S
s
1
i
fM
7
o
00
I
-a-
1
"o
rt
o
if
11 g
0
1
O
0
H
|i
11!
•Z* SJ O
s
S
Q
u
?
"3
^ o
jjj
^
^,
a
s
0
(L
CO
o
fH
"g
-
=»
^
I
S
T
—
S
*?
c'0
§"rf
^
zo
a
s
"
s
S
0
!
<=»•
J
s
^
"0*0
1IN
1*8
3"^
•£
•
§
.
a
S3 -
% :
.
I
_^
°L
^
&
§
vO
1
I
|c
NO
8
_
3
v^.
„
1
RMANo..
Material. .
I.
S
6
1
1
1-
i1
..£
s53
Operating
lambertj
Li A!I t sour
J
Q
V =2
^
1
Cj
"c
0
Runge of fi
Q
Reaiarka . ,
15-40
ELECTRO-OPTICAL DEVICES
Wavelength vs energy plot?
32 100*32 45
Representative spectral distribution curses of the major cathode-ray-tube screens are
shown in Fig. 10. The numbers near the peaks of the emission bands of individual phos-
phors are the heights of the bands relative to the peak of the cathodoluminescence band
of a-Zn2SiO4:Mn (PI) which is arbitrarily set equal to 100. The visible cathodolumines-
cence efficiency of conventional Pi screens is about 3 candles per watt at 6 kv and 1 micro-
ampere per square centimeter. The spectral distribution curves of the white-emitting
P4 (monochrome-television) and P6 (color-television) screens may vary considerably
among different manufacturers, since there are many possible ways of producing equiva-
lent-appearing white colors. The optimum white is yet to be decided by popular approval,
although P4 screens are presently standardized at a color temperature of about 6500-7000
deg Kelvin. The P4 screen is usually a two-component mixture of blue-emitting and
yellow-emitting phosphors [all-sulfide(selenide) or sulnde(selenide) -silicate]; the P6
screen is usually a three-component
mixture of blue-, green-, and red-emit-
ting sulfide- (selenide) phosphors.
The optimum screen thicknesses for
cathode-ray tubes vary from about 1
mg/cm2 for phosphors having average
particle sizes less than 1 micron, to 22
mg/cm2 for cascade-screen (P7 and
P14) phosphors having average parti-
cle sizes near 15 microns. The evapo-
rated P10 (KC1) screen thickness is
about 12 microns. These thicknesses
are for operation below about 10 kv
and must be increased for higher volt-
ages according to eqs. (10) and (11).
The strontium-containing phosphors
listed at the bottom of Table 1 are
infrared-stimulable materials which
have quite deep electron traps (of the
order of 1 electron volt) . These mate-
rials can store most of their latent
phosphorescence energy for several
days, even at room temperature. Effi-
cient release of the stored phosphores-
cence energy is obtained by irradiating
the previously excited material with
near-infrared which may be varied in
intensity to alter the normal concave-
upward decay of the phosphor. These
phosphors are good photolumineseent
materials but are relatively inefficient
under cathode rays. By cocrystalliz-
ing sulfate ions in copper-activated
zinc sulfide phosphor, an unusual
FIG. 10. Representative Spectra of Seine Cathode-ray-
tube Screens. P4 and P6 screens vary considerably
among different manufacturers.
infrared-quenchable phosphor is produced which affords long phosphorescence plus the
ability to decrease or terminate the phosphorescence by quenching with infrared at an
arbitrary instant during the decay time. Infrared-sensitive phosphors may be used to
store information for controllable time intervals or to convert positive images into negative
images (or vice versa) .
The intensity and duration of phosphorescence after cathode-ray excitation is generally
less than that obtained after excitation by photons. Cathode-ray-excited phosphorescence
may be increased by using the cascade principle. The cascade principle involves construct-
ing a stratified-layer screen wherein an efficient photophosphorescent material is covered
with a layer of an efficient cathodoluminescent material whose emission band overlaps the
excitation band of the photophosphorescent material. By this method, cathode-ray
energy is intermediately converted into photon energy which is more efficient in exciting
phosphors to produce phosphorescence. Cascading may be used also to excite cathode-ray-
modulated photoluminescence in materials, such as the infrared-stimulable phosphors,
which are inefficient under direct cathode-ray excitation. The P7 and P14 screens are
examples of practical cascade screens which were devised for radar cathode-ray tubes.
ELECTRON GUN
15-41
BIBLIOGRAPHY
1. Leverenz, H. W., Cathodoluminescence as Applied in Television, R,€.A. Rev., VoL V, No. 2, 131-
176 (October 1940).
2. Leverenz, H. W., Luminescence and Tenebrescence as Applied in Radar, R.C.A. Rei., VoL VII,
No. 2, 199-240 (June 1946).
3. Some of the data mentioned herein were obtained during the coarse of Contracts NDCrc-150
and OEMsr-440 between the Office of Scientific Research and Development and the Radio
Corporation of America. A more complete account, •with over 400 further references, may be
found in H. W. Leverenz, Final Report on Research and Development Leading to New and
Improved Radar Indicators, Report NDRC-1 4-498, June 30, 1945, obtainable from the Office
of the Publication Board, Department of Commerce, Washington, D. C. (PB254S1).
4. Leverenz, H. W., Luminescent Solids (Phosphors), Science, VoL 109, No. 2826, 183-195 (Feb. 25,
1949).
5. Leverenz, H. W., An. Introduction to Luminescence of Solids, Wiley (1950).
6. Fonda, G. R., and Seitz, F. (Editors), Preparation and Characteristic* of Solid Lumw¢ Male-
rials, Wiley (1948).
CATHODE-RAY TUBES
By L. E. Swedlund
The cathode-ray tubes considered herein are those electron tubes in which a relatively
low-current electron beam of small circular cross-section is focused on, and deflected
across, a luminescent screen. Their
Accelerating First Second _- v
electrode artode anode ^^^^^^^ ^
x \ ~f Luminescent
JJJ « . —
IjuM
Grid
Gross over
Masking
aperture
T
principal applications are in tele-
vision receivers, oscillographs, and
xadar-type indicators. Their great
value is the ability to display varia-
tions in voltage and current without
the limitations of mechanical inertia,
and their relatively low cost. Except
for a few specialized designs, they are
sealed-off, high-vacuum tubes, hav-
ing an electron, gun with a heater-
type, oxide-coated cathode located
in. the neck of a cone-shaped glass
bulb. A luminescent screen, is deposited in the large, nearly flat end of this cone. Figure 1
shows an electrostatic-focus, electrostatic-deflection oscillograph-type cathode-ray tube,
and Fig. 2 a magnetic-focus, magnetic-deflection tube, for television image reproduction.
Magnetic focus is very seldom used with electrostatic deflection, but electrostatic focus
is often used with magnetic deflection. The principal parts of the cathode-ray tube are
the electron gun, the bulb, and the luminescent screen.
FIG. 1. Hectrostatic-focus Electrostatic-deflection Cath-
ode-ray Tube
19. ELECTRON GUN
The design of the electron gun is based on the principles of electron optics outlined in
Section 14. However, owing to the complex nature of the electron paths, particularly in
the region of the grid and cathode, and to the
large number of interrelated factors, much of
the design is based on experimental informa-
tion. The active cathode surface is a small,
flat, oxide-coated nickel surface normal to the
gun axis. Directly heated, high-temperature
cathodes are occasionally used in high-voltage
tubes to withstand better the effects of positive-
ion bombardment. A control grid having a
round aperture of approximately <XG4-ih. diam-
eter is spaced as closely as practical to the
cathode. As the spacing may amount to only
0.002 in. when the cathode is hot, it is difficult
to hold this spacing constant from tube to tube. This small variation in spacing results
in a fairly large variation in control-grid voltage for beam-current cutoff. The control grid
is nearly always designed to operate at a negative potential with respect to the cathode.
The beam is accelerated by means of a screen grid, first anode, and second anode; by a
screen grid and anode; or directly by an anode to full-beam potential. In each case, the
Cath&de /
Cross-over
FIG. 2. Magnetic-focus Magnetic-deflection.
Cathode-ray Tube
15-42 ELECTRO-OPTICAL DEVICES
spacing between the first accelerating electrode and the control grid is adjusted to provide
about the same accelerating field at the cathode. Maximum beam currents of the order
of 1 milliampere are drawn at zero bias, and the specified control-grid bias for beam eutofT
varies from approximately 20 to 100 volts.
OPERATION OF THE ELECTRON GUN. The field above the cathode draws the
electrons into a focus in a few millimeters' travel. In this field they cross over, and beyond
it they travel in straight paths until they enter the final focusing field near the end of the
gun. Here the electrons are made to converge to a second focus or cross-over at the
screen. The final focusing field or electron lens may be either electrostatic or magnetic.
The electrostatic lens consists of coaxial cylinders, apertured disks, or a combination of
both. These components are always mounted inside the tube. The magnetic lens is
always mounted outside the neck of the tube and usually is a coaxial coil encased in an
iron shell except for a short axial magnetic gap on the inside surface. In both cases a
very good degree of rotational symmetry is required. The usual error due to any lack of
symmetry is astigmatism, which results in an elliptical shape when the spot is focused.
Electrostatic focus is adjusted by varying the first-anode voltage. The first-anode voltage
is usualb' about one-fifth the second-anode voltage. Magnetic focus is adjusted by chang-
ing the magnetic field in the region of the electron beam. This is done by varying the
current in an electromagnetic focus coil or by varying a magnetic shunt in a permanent-
magnet focus unit.
ELECTROSTATIC DEFLECTION. Figure 1 shows two pairs of deflecting plates at
right angles to each other at the exit of the electron gun. The average potential of each
pair should be near that of the second anode of the gun since a difference will produce a
focusing effect. Since such focusing produces a strong astigmatic effect it is sometimes
possible to adjust their average potential to counteract astigmatism in the electron gun.
Most tubes, however, are so well made that such correction is not needed. The best uni-
formity of focus is attained with symmetrical or push-pull deflection. It is possible to
connect one plate of a pair to the second anode and apply voltage only to the other at
the expense of focus and sometimes linearity of deflection. When the deflection plates
are parallel the deflection can be calculated from the following equation.
-38
where h is the deflection from the center, L is the plate to screen distance, I the deflecting-
plate length, Vd the difference in potential between the plates, Vb the second-anode or
beam voltage, and d the spacing between plates. In order to provide maximum sensi-
tivity, the plates are usually shaped to follow the contour of the deflected beam. The
expression for deflection becomes more complex but has about the same proportionality
factors.
MAGNETIC DEFLECTION. Magnetic deflection is accomplished by placing a mag-
netic field at right angles to the beam path. This field is usually provided by a pair of
coaxial coils placed on opposite sides of the neck in order to produce a nearly uniform
deflecting field. The beam moves at right angles to the magnetic field in a direction
indicated by the familiar left-hand motor rule, remembering, however, that conventional
current flow is opposite that of electrons. Unlike electrostatic deflection, it is possible and
advantageous to place a second pair of coils for orthogonal deflection in the same region
as the first. A combination of deflection coils is known as a deflection yoke and is ordi-
narily designed to meet the rather specialized requirements of television. Magnetic pole
pieces and return paths are sometimes provided to decrease the current required by reduc-
ing the reluctance of the magnetic path. The deflection h at the screen for a magnetic
field of length Z having uniform flux density of B at a distance L from the screen, and
for a final voltage J?&, is
, 0.298 X W^BIL
h •• — (2)
VVb
Since there is a large air gap in these coils, the flux density is proportional to the current
and thus deflection is proportional to the current. Although some approximations have
been made, this equation holds well up to 60° total deflecting angle. It is seldom desired
that the field be uniform across the neck because the screen is usually not properly curved
to produce a pattern which looks rectangular. In the reflective optics projection system,
for example, the pattern is made to "barrel" slightly to correct for "pin-cushion" distortion
in the optics (see Section 14) .
COMPARISON OF MAGNETIC AND ELECTROSTATIC DEFLECTION. In com-
paring eqs- (1) and (2) for electrostatic and magnetic deflection, it is to be noted that,
with an increase of beam voltage, deflection decreases with the anode voltage in the former
BULBS FOR CATHODE-RAY TUBES 15-43
and as the square root of the anode voltage in the latter. Thus, magnetic deflection be-
comes relatively more favorable as the voltage is raised. In television, this, plus relatively
better focus and economic factors, sets the dividing point at about 5 kv. Electrostatic and
magnetic deflection are occasionally combined in one tube, though tubes designed spe-
cifically for this type of operation have not found many applications.
DEFLECTION DEFOCUSING. Deflection is accompanied by a deterioration of focus
known as deflection defocusing. It appears as an elongation of the spot in the direction of
deflection in electrostatic deflection and as an elongated and rotated spot in magnetic
deflection. It increases approximately as the square of the deflecting angle. Thus deflec-
tion distortion limits the deflecting angle and indirectly the beam current because the
amount of current which can be focused into a given size spot is determined by the size
of the beam as it leaves the gun. For high currents and wide deflecting angles the deflec-
tion distortion is five to ten times as great with electrostatic deflection as with magnetic
deflection. As a result, electrostatic-deflection tubes are designed for smaller focused
currents and narrower deflecting angles than magnetic-deflection tubes. The change of
focus due to the increase of gun to screen distance with deflection is small compared to
deflection defocusing even with fiat screens. But, since deflection defocusing also produces
a shortening of the image focal distance, it is possible to make a small amount of compensa-
tion by slightly underf ocusing the beam at the center of the screen. This effect is usually
so small that it is not worth while to modulate the focus voltage in synchronism with scan-
ning to improve the uniformity of focus,
20. BULBS FOR CATHODE-RAY TUBES
The bulb of the cathode-ray tube must meet specialized requirements for mechanical
strength, dimensions, optical quality, and electrical insulation. Special grades of glass are
needed to meet these demands. Although the bulb has to withstand only atmospheric
pressure (15 Ib per sq in.) it is good practice to design for a breaking strength of 60 Ib or
more per sq in. This is done to avoid failure due to slight scratches, temperature shock,
and aging. Great care should be exercised, particularly in handling the larger tubes, to
protect personnel from flying glass in the event of accidental implosion. Generally the
zone of highest stress in a bulb is near the rim of the face. Here the outside surface of the
glass is in tension, in which it is weak, and so particular care should be taken to avoid
scratches and shocks in this zone. In the past large bulbs were usually made of heat-
resisting, low-thermal-expansion glasses, but because of both cost and optical quality most
bulbs are now made of a soft glass. For all but the low-voltage oscillograph-type tubes,
this is a lead-type glass in contrast to the usual lime-type soft glass. It is chosen to obtain
high electrical resistivity. Large bulbs are mass-produced by pressing parts which are
fused together. If the surface must be very good and accurately shaped, as in projection
type tubes, the face plate may be ground and polished before sealing to the bulb.
LIMITATIONS IMPOSED BY THE LUMINESCENT SCREEN. The luminescent
screen is a very important part of the cathode-ray tube. (See articles 15—18.) The limita-
tions and requirements of the luminescent screen have an important bearing on gun-design
problems. Both the amount of current that can be sharply focused and the amount that
can be utilized efficiently by the screen are limited at low voltage. High brightness,
consequently, has to be obtained by raising the beam voltage applied to the screen. Al-
though raising the anode voltage improves the focus and screen efficiency, it also increases
electrical insulation problems, introduces screen charging, and requires higher deflection
energy. Specially developed, low-current, high-voltage power supplies which have low
cost, compactness, and safety have made this problem less difficult.
SCREEN SIZE AND BRIGHTNESS. When the screen size is increased without chang-
ing the gun or deflecting angle, the anode voltage must be raised to maintain the same
number of lines resolution and brightness. This is due to the fact that the size of the
focused spot increases with bulb length and that the beam energy per unit of screen area
determines the brightness. Projection tubes require the highest screen brightness and are
therefore operated at the highest voltages. Luminescent screens are very thin and thus
have a very small thermal storage capacity. Great care must be taken not to move the
beam slowly or over too small an area. With a small overload the screen may be damaged
only temporarily, as by overheating, or to a light "burn" which gradually fades out. The
total time of screen bombardment during the life of a tube is surprisingly small. Consider a
television tube scanned with a 525-line raster. This provides roughly 360,000 picture
elements; and so, neglecting blanked-out return line time and modulation, each element
of the picture area is being bombarded only l/360,000th of the time. One thousand hours
amounts to 3,600.000 seconds. Thus in a representative tube lifetime, the screen has been
15-44 ELECTRO-OPTICAL DEVICES
bombarded less than 10 seconds. However, during this short time it is bombarded at a
very high momentary energy density; for example, in a 5-in. projection tube it amounts
to 25 kw/cm2.
DISCHARGE OF SCREEN. Luminescent screen materials are good electrical insulators
and are prevented from charging up negatively under electron bombardment only by
virtue of a secondary-to-primary electron-emission ratio equal to or greater than unity.
The range of voltage where this is true varies with the type of screen material, its manu-
facture, and application. Under favorable conditions screens can be discharged by second-
ary emission over the 500 to 25,000 volt range. At the upper end of the range not all
phosphors can be used and a charge of several thousand volts may build up on the screen,
thus reducing the effective screen voltage. In general, secondary emission becomes poorer
at low current density and with use. Poor secondary emission at low voltage causes the
screen to charge up enough to deflect the beam off the screen. For example, trouble is
likely to occur if beam current flows to the screen while the anode voltage is building up.
A charge is then built up before the screen is bombarded with full-voltage electrons. At
the upper end of the range the light output fails to increase at the normal rate with voltage
increase and the pattern may become unstable. The effects of poor secondary emission
may be overcome by mounting the phosphor on a conducting surface and, above about
7000 volts, by placing a very thin, light metal back on the luminescent screen. The metal
back is especially desk-able because it can be made light-reflecting in order to utilize the
light ordinarily lost through the back of the screen. It can also serve as an effective barrier
to negative ions.
ION SPOT IN SCREEN. Ion spot in the screen is a problem, particularly in magnet-
ically deflected tubes. It is the area in the luminescent screen which has been damaged
by negative-ion bombardment. The screen is damaged almost altogether by the negative
ions which form in or near the cathode surface when it is bombarded by positive ions. The
. rate of damage increases with voltage, but it is
* most noticeable at about 7 kv because above this
voltage the electrons begin to penetrate below
the damaged surface layer of the screen. It is
^t^Tilft Electrons? ' greatly affected by the amount and kind of gas
.J-fffF" j j 22L5!Jj!e left in the tube, but it is almost impossible to
eliminate ion damage completely by evacuation
and gas getters. Because electrostatic focusing
is independent of mass and magnetic focusing is
not, electrostatic focus guns focus the ions, thus
forming small ion spots rather quickly whereas
magnetic focus tubes form large ion spots slowly.
Initially the small spot is more objectionable, but
with time the large spot becomes more objection-
able. In addition to the metal-backed screen,
which is rather expensive to apply to low-voltage
B. "Tilted lens" gun * tubes, there is another effective solution known
FIG. 3. Sectional Views of Ion Trap Guns *» ** "io11 W electron gun. Figure 3 shows
two constructions of this idea. Both are simpli-
fied modifications of the mass spectrograph. The combined beam of ions and electrons is
directed off the center of the gun into a trap in A by bending the anode and accelerator
and in B by means of a tilted electrostatic lens. In both, a magnetic field is applied to
restore the electrons to the axis. The secondary magnetic field used in construction B is
useful not only in aligning the beam with the gun axis but also in overcoming the slight
mechanical misalignments that may be present.
21. CHARACTERISTICS OF THE IMAGE
SPOT SIZE. The image detail or resolution is determined principally by the size of
the focused electron image on the screen. Contrast and gram, size of the screen may also
be factors. The spot does not have a definite edge but decreases in brightness from the
center approximately as a segment of a sine wave. When the beam scans a television-type
raster it is found that, when the lines overlap to the point where the brightness is half that
of the center, the line structure practically disappears, For this reason it is convenient to
express spot size as the width at these half-brightness values. This is the basis of the
"compressed raster" method of measuring spot size sometimes used for oscillograph-type
fetfees. However, the rate at which the brightness falls off toward the edge of the spot
is «pGrfcaa?fc m determining the resolving power, and so for television reproduction tubes a
CHARACTERISTICS OF THE IMAGE 15-45
resolution pattern signal which takes this into account is generally used. (See Fig. 10,
p. 15-25.)
The resolution pattern has sets of spaced black and white lines usually converging in
wedges along with circles and bars for other tests. The limiting resolution is denned as
the point where the black and white lines merge. It is important that the black to white
grid signal level be maintained beyond the value of resolution being read. If the reproduc-
tion tube is not to limit the resolution of the television signal noticeably, its limiting
resolution should be about three times that of the television signal. The resolution is best
at the center of the raster and poorest in the corners, and since it depends on the deflection
yoke it may vary with the direction of scanning. Its value is usually expressed in terms
of the number of black and white lines required to fill the vertical height of the raster.
In photographic and optical literature it is generally the practice to count only the number
of black lines per unit of length.
CONTRAST. The ability to see an image on a screen depends not only on the bright-
ness of the trace but also on the ratio of this brightness to the background brightness. This
is known as the brightness contrast ratio. This ratio, also sometimes referred to as con-
trast range, determines the number of distinct half tones which can be reproduced. Its
value depends not only on the inherent characteristic of the screen but also upon the area
and distribution of illumination in the screen. The minimum or limiting value of contrast
ratio can be found by uniformly scanning all but a small black spot in the center of the
raster. A contrast ratio representative of large areas can be found by scanning half the
picture area and measuring the brightness in the center of each half.
GAMMA. The term gamma is borrowed from photographic practice to designate the
half-tone characteristics of a television system. Over the brightness range useful for tele-
vision reproduction the eye recognizes brightness differences as percentage increases in
steps of 1 to 2 per cent. For this reason it is convenient to plot the grid drive versus light
output of a picture tube on log-log scales. The slope of this curve is known as the gamma.
In the same way each part of the system from the light in the scene on through the ampli-
fiers has a gamma value. The overall gamma is the product of those of the series of ele-
ments. Unity overall gamma, which is usually desired, then represents brightness values
in the image proportional to those in the scene. The gamma should be uniform over the
whole brightness range for accurate reproduction, but it is usually less at the low and high
brightness levels, as is also true in photographic reproduction. It is the practice in photog-
raphy to refer to gamma as "contrast." This should not be confused with contrast ratio.
It has become the practice to mark the d-c bias and the signal controls of television
receivers as "brightness" and "contrast" respectively. However, both controls affect
the gamma and brightness. Overbiasing increases gamma by eliminating detail in the
shadows; underbiasing decreases it by "washing out" shadow detail. Average brightness
varies with d-c bias. Increase in brightness by signal increase is usually limited by the
increase in spot size or amplifier overload. This loss of detail and contrast in the highlights
is sometimes referred to as "blooming." In a picture tube the average gamma varies from
3 to 2, depending on the amount of masking in the gun. Correction to match the gamma
of a standard transmitted signal must be done by introducing suitable curvature in the
amplifier input versus output characteristic.
POST ACCELERATION. The beam is sometimes accelerated after deflection in order
to increase the spot brightness without a proportionate increase in deflection energy. For
this purpose the bulb conductive coating is separated and brought out to a third anode
terminal. It has been applied only to electrostatic deflection tubes because little or no
gain results when it is used with magnetic deflection. Post acceleration results in a focus-
ing action which tends to bend the deflected beam back to the axis. There is also
a small amount of focusing action on the spot which is readily corrected by raising
the first anode voltage a qm»-fl amount. In a typical post-accelerator-type oscillograph
tube the deflection voltage must be raised 20 per cent when the third anode is in-
creased from equal to double the second anode voltage. This increase in deflection voltage
is accompanied by an increase in deflection defocusing so that the sharpness of focus is
not as good as an equivalent non-accelerator tube whose screen voltage is the same. The
deflection sensitivity also will not be as much less as indicated on the comparative tests
on the accelerator tube because the deflection plates can be designed for closer spacing.
However, the gain in brightness and deflection sensitivity along with the fact that the high-
voltage power supply is grounded between its negative and positive terminals often justifies
the higher cost of a tube of this type. The accelerator ratio is ordinarily limited to about
2, but where very high spot brightness is needed tubes may be designed to operate up to
a ratio of 10 times.
PHOTOGRAPHY OF CATHODE-RAY-TUBE TRACES. A permanent record is
sometimes needed, and when a tracing of the pattern on the tube cannot be readily made
15-46
ELECTRO-OPTICAL DEVICES
it can usually be photographed. Unless a time exposure can be made the brightness level
suitable for viewing must usually be increased by raising the beam current and possibly
by raising the screen voltage. Luminescent screens such as the P5 and Pll are particularly
suited to photography. The blue light of these screens provides energy where the film is
most sensitive. The lower-cost "color blind" films may sometimes serve nearly as well
as the orthochromatic and panchromatic films. Since the Pll screen has approximately
10 times the photographic and visual efficiency of the P5 screen it is preferred, but occa-
sionally its longer persistence may be a limitation. The proper exposure depends on lens
speed, film sensitivity, screen size, spot brightness, and spot velocity. Tables suitable for
estimating the best exposure are available from tube manufacturers, but usually a suitable
value can be found from a few test exposures. Single television frames can be photo-
graphed with a hand camera having a fast lens and by using high-speed panchromatic
film. For motion-picture records the camera must be exposed in synchronism with the
frame frequency.
22. TELEVISION CATHODE-RAY REPRODUCTION TUBES
Cathode-ray tubes for television image reproduction are known as picture tubes or
kinescopes. In directly viewed tubes the size of the screen largely determines the cost and
operating voltage. Below a diameter of 7 in. the reduction hi cost is not great and the
image size is too small for comfortable viewing. Ten-, fifteen-, and twenty-inch bulbs
provide images in steps of double-sized areas. Intermediate sizes such as 12 in. are also
used. In the largest bulbs the economic limit for evacuated glass bulbs is reached. Larger
images have to be produced by optical projection from a small screen tube. This small
tube, known as a projection tube, must produce a much brighter image to illuminate the
larger viewing screen and to make up for the losses in the optical system and so is operated
at a higher anode voltage.
Table 1. Television Picture-reproduction Cathode-ray Tubes
Type
Size, in.
Typical Operation
Comments
Nominal
Diam-
eter
Length
Heater
Anode
2,kv
Anode
1, volts
Grid
2,
volts
Control
Grid
Cutoff
Focus
Volts
Amperes
5TP4. . . .
5
113/4
6.3
0.6
27
4900
200
-70
ES
Reflective optics pro-
jection
7CP4. . . .
7
137/lfi
7
1365
250
-45
ES
Monitor use in day-
light
7DP4....
7
141/16
6.3
0.6
6
1430
250
-45
ES
Small size receiver
7EP4....
7
151/2
6.3
0.6
2.5
650
-60
ES
ES deflection, low-
cost receiver; see
oscillograph tubes
for deflection factors
7JP4....
7
141/2
6.3
0.6
6
1000
-120
ES
ES deflection for low-
cost receiver; see
oscillograph tubes
for deflection factors
7HP4....
7
13
6.3
0.6
6
250
-55
M
Small size receiver
IOAP4...
10
171/2
6.3
0.6
6
-60
M
Bent gun ion trap
IOBP4. . .
10
175/8
6.3
0.6
9
250
-45
M
Directly viewed, tilted
lens ion trap
10CP4. . .
10
165/8
6.3
0.6
8
250
-45
M
Directly -dewed
10EP4. . .
10
175/g
6.3
0.6
8
250
-45
M
Directly viewed, tilted
lens ion trap
10FP4...
10
17
6.3
0.6
9
250
-45
M
Directly viewed,
metal-backed screen
I2JP4...
12
171/2
6.3
0.6
10
250
-45
M
Directly viewed
15AP4...
15
203/16
6.3
0.6
10
250
-45
M
Large directly viewed
15BP4. . .
15
19
6.3
0.6
12
250
_45
M
Large directly viewed,
rectangular face
2QBP4. . .
20
283/4
6.3
0.6
15
250
-45
M
Large directly viewed
Note The above table includes the tubes commercially available. Developmental tubes and those recommended for
repJacesnent oaly are not included. However, some of the tubes in these lists are in fact outmoded and will in time
beeomse obsolete. Owing to changes and additions which are constantly being made, up-to-date and more detailed
iilQnaaiatkm sbauld be obtained from tube manufacturers or their agents.
Tiw* deflecting angle in. a!i &e above tubes is 50° or slightly above. All use P4r-type screens.
BIBLIOGRAPHY 15-47
DEFLECTION AKD FOCUS OF PICTURE TUBES. Magnetic deflection is used for
all but the smallest television picture tubes because it permits the use of wider deflection
angles and higher beam currents. Owing to the desire for short overall length, particularly
in the large tubes, the deflecting angle is made as large as practicable. Fifty-degree total
angle has been found to provide a good compromise between focus uniformity, beam
current, and deflecting power. Both magnetic and electrostatic focus guns are used, the
former being favored for directly viewed tubes and the latter for project ion-type tubes.
At the high anode voltages used in the projection tubeT energy for the focusing coil becomes
a more important factor and the coil is also difficuli to mount in the reflective optics system
generally used for projection. The highest-voltage power supplies tend to have the poorest
voltage regulation, so that a first anode which can be held in focus by means of a tap on
the bleeder across the high- voltage supply is quite desirable. The bulb size of projection
tubes is limited by the cost and bulk of the optical system used with them. For home use
a 5-in. bulb and 27 kv appears to be an economic choice. For intermediate and theater-
size images larger tubes and much higher operating voltages are justified.
23. OSCILLOGRAPH-TYPE CATHODE-RAY TUBES
These tubes are nearly always of the electrostatic-focus, electrostatic-deflection type.
Their largest field of application is in low-voltage oscillographs for visual observations.
These operate in the range of 500 to 2000 volts, but, for the observation and photography
of high-frequency transients, anode voltages up to 30 kv may be used. The higher bright-
ness and sharper focus afforded by higher-voltage operation are desirable but it results
in lower deflection sensitivity and higher cost tubes and accessories. The signal must
usually be amplified, and because a wide band width is desired the gain per stage is low.
The size of the screen also influences the choice of anode voltage, since the energy to the
screen should go up with its size. Conversely, with a given anode voltage, a small-diameter
tube may indicate more detail than a large screen tube. Of the factors determining oscillo-
graph-tube performance, deflection sensitivity is the most important. Deflection sensi-
tivity is customarily expressed as the number of millimeters7 deflection at the screen per
volt (d-c) of deflection voltage. The reciprocal of this term, the deflection factor, is usually
expressed in d-c volts per inch of deflection. The latter term is favored for design vork.
Spot size and contrast are next in importance. Grid modulation sensitivity is of relatively
less importance than in television. It is desirable that the focus remain sharp -while the
beam current is varied, so most oscillograph-type tubes utilize an electron gun requiring
essentially zero-first-anode current in order to avoid the effects of voltage regulation in
the first anode circuit.
HIGH-FREQUENCY DEFLECTION. When the deflecting electrode leads must have
minimum inductance, capacitance, and coupling to other leads, they are brought directly
through the neck of the bulb. This is also of value when very wide frequency band ampli-
fiers are used. For frequencies of about 100 megacycles and above it is necessary to take
into account the electron transit time through the plates. Special tubes with short-length
plates and high beam voltage have been used to record frequencies as high as 10,000 mega-
cycles per second.
MULTIPLE GUN OSCILLOGRAPH TUBES. Oscfflograph-type tubes with two or
three independent guns and deflection systems are available for simultaneously producing
two or more traces. Owing to their more complex construction their cost is higher than that
of the equivalent number of single tubes. An electronic switch or the simultaneous use of
two or more tubes is sometimes satisfactory.
RADIAL DEFLECTION TUBES. Radial deflection tubes have a rod-type deflecting
electrode extending through the face into the middle of the cone. The deflection sensitivity
of the rod decreases as the square of the deflection so that it cannot readily be calibrated.
It is used principally to make a marker pip on a circular time base.
BIBLIOGRAPHY
Law, R. R., Contrast in Kinescopes, Proc. I.R.E., August 1939, pp. 311-524.
Bachman, C. H., Image Contrast in Television, Gen. Elec. Rev., Vol. 48, No. 9, 13-19 (September 1945).
Feldt, Rudolf, Photographing Patterns on Cathode-ray Tubes, Electronics, February 1944.
15-48
ELECTRO-OPTICAL DEVICES
Table 2. Cathode-ray Tubes and Their Characteristics
OHciLLoaitApnvnrrH TUBES
ELECTROSTATIC-DEFLECTION TYPES
Comments
11 i 8 3? 3
•a e! , i- ss s
8 «§ § i i* ^i,
| If &t? =•§ If 2
2 c p £ u o & £ tS °tj £ ^ fl c fl *••
i il 1 1 j |jj *|i || mi
1 || 1 1 !| i; l|l P llj|
1 2 a a s-S^ s s 2! a sf ali-as g^-S §sss g s 2 g
Illll!ll1l1ll!lilll-l-5lll-f-gllll
2'3"3'3*o"5'H"5 £"S"S'S o S'S'ti'M^'S'SS i:3""'S'SiS'"'2's'°
!3oco3!o3oSo^o5troS m^ °oos "oooo
flowed by "A" indicate improved designs which are interchangeable with the old; however, the reverse ia not necessarily true. In the
on tubes it indicates the change to zero-first-anode current gun.
MAGNETIODEFLECTION-TYPE OSCILLOGRAPH TUBES
<n
1
ndicator
ndicator
on monitor
ndicator
ndicator
ndicator
Illlll
a
P
oooooo
s
.2
*+3
a
O
'a
h
o
ssasss
Other
Screens
Listed
ts— " ts ri IN JN"
Control
Grid
Cutoff
om^tnoow^
1 1 I I 1 1
Typical Operation
idq
S-S£S¥r3gS?SS§S£S S3 £ ?SSg SS5I3
(N
•§
o
oooooo
gpQ
* w ^
osk
j«.^vjcn— o*n«^«^csooC"~0v(00sON for>> ^ tf"30^ «t>— co
!
NO
fA
Is?
e fri
a°s
NOOOOOO«AOOOOOOOt>-OO«rY OO O OO>QO COOO«
tf\vovO'<rtn'O'<-so»Otf%%O'^i«rkiAtnvOr>. «vO -o -rcs»o ^'^•«AON
i i 1 1 i i ! i 1 ! 1 i 1 1 M I M 1 III I 1 1 I
o
ooo.«o«,o^o*.«o«u^o o^ « o«o o^^r.
<N
1
oooooo
oooooo
oooooo
N
•§
Or>»
•<
ooooooooooooooooo oo o ooo oooo
OOOOOOOOC300000000 00 0 000 ggOg
""*""" ~~ ~ "~"~ "" ~~0
Heater
£
,0™.
o
T3
Otfi
<3
0 0 00 00 0 0
o o oo oo o o
o o oo oo o o
<«• T •«••«• T^- >f
oooooo
S E
1^
0>0^^~^0«0^000-^vOOvO ^>0 xO 0 ONO-0
00
'o
OOOOtVOOOOO^OtNOOOO OO O OfSCS OO«SO
**>*>*>**
i-i ac
3
^cnm^.n^m^cnrn^fO^rAcA^^ c*m <* n^ <*^^
c
!
-cnmr^^o
0^vOvO<NsOvOsOsO^^O<NOOvOO OM3 O sOCNC4 vOvOfS^O
5
1
I
«S5« || « 3w«^ ^ < ^^ ^s
Note: ItMA tube numbers i(
case of the electrostatic-deflecti
Nominal
Diameter
.™»J,
Nominal
Diameter
-««««««««««««.««« w « ««« ....
a
<jj< IP;
_*
: :< '•«* '•< '• '• • • '<<^ '•'• '•'•'• '•'•••
^ ;^S il : : :| iSRfe :: :g^ : :g^
|S||^||||||||^|B| || i ||l mi
CATHOBE-RAY-TUBE DISPLAYS 15-49
24. CATHODE-RAY-TUBE DISPLAYS
By T. Seller
A cathode-ray-tube display is a means of presenting information concerning a signal
(which, may be any quantity that can be put into the form of an electrical voltage) in
terms of one or more independent variables on which the signal depends. Usually at least
one of these variables is an explicit or implicit function of time. The variables are repre-
sented by displacements along cartesian or polar coordinate axes; the displacements are
usually periodic, a single traversal along any axis being called a "sweep."
A display is said to be deflection-modulated if the signal produces a lateral displacement
of the electron beam from some base line or sweep; it is said to be intensity-modulated if
the signal voltage is used to increase or decrease the intensity of the electron beam. A de-
flection-modulated display is used when quantitative information regarding the nature of
the signal is required, for an intensity-modulated display can at best yield only qualitative
information regarding the signal strength or shape. An intensity-modulated display offers
the advantage of being able to present the signal in terms of two variables, rather than
the single variable (usually time) of the deflection-modulated display. Well-known ex-
amples of these two general types of display are the usual form of cathode-ray oscillograph,
(deflection-modulated) and the television display (intensity-modulated).
Many different types of display were developed in connection with the applications of
radar during World War II. In many of these an attempt was made to present on the two-
dimensional surface of the CRT screen information regarding the signal involving three
variables, for example, range, azimuth, and elevation. The designation and geometry of
these various display types are shown in the following pages.*
* For a more complete discussion of the subject, see: M.I.T. Radiation Laboratory Series, Vol. 22,
Cathode Ray Tube Displays, McGraw-Hill Book Co., New York, 1947.
15-50
ELECTKO-OPTICAL DEVICES
Lkieartfrae base
Type A
A deflection-modulated display, commonly used with electro-
static-deflection types of cathode-ray tubes. Consists of a linear
horizontal time base, with the signal voltage applied to give a
vertical deflection. Used primarily to measure the time of
occurrence (in radar, the range) of the signal, as well as its
shape and strength. There are many modifications of this basic
display type (see types K, L, Mt N, O, R).
TypeB
An intensity-modulated (radar) display in which the horizon-
tal sweep is synchronized with the antenna direction, and the
vertical sweep is a linear time base repeated with each trans-
mitted pulse. The received signal is applied to the control grid
or to the cathode of the CRT in such a polarity as to brighten
the screen. The display has a large distortion from a true map
when the range sweep starts with the transmitted pulse and a
large azimuth sector is displayed. By delaying the range sweep,
and by simultaneous proper control of the azimuth expansion,
a good approximation to a true map may be obtained, over a
limited region. Such variations are called "delayed B-scans"
or "micro-B scans."
TypeC
An intensity-modulated display, with azimuth as the horizon-
tal coordinate and elevation as the vertical. This is the tele-
vision type of scan. In radar, principally used in aircraft for
location of other aircraft. Gives no indication of range. This
type of indication is very bad from the signal-to-noise ratio
standpoint, unless "range-gating" of the signal (from informa-
tion obtained from a type B display, for example) is possible.
Number of horizontal scanning lines used in radar is quite small,
and signal appears on several scans because of wide angle of
transmitted beam.
CATHODE-RAY-TUBE DISPLAYS
15-51
TypeD
A modification of type C indication, for airborne radar, giving
crude elevation information (widely separated elevation lines),
but also yielding range informal ion. As any line is scanned
slowly from left to right, a short range sweep extending from
one elevation line to the next is simultaneously applied. Thus,
for the signal shown, the pertinent data are: azimuth, 30° to
right; elevation, -j- 10°; range, 2 miles (assuming distance be-
tween elevation lines is equal to 3 milesk
Listed for record purposes only; never used in production.
Range
TypeE
Similar to type B, but with range as the horizontal coordinate,
and elevation angle as the vertical. Presents a distorted vertical
cross-section, since lines of constant height are curved, as indi-
cated. ChieSy used where elevation angle (and not height) is
of importance.
Down
TypeF
Sometimes called a "spot" error display. No sweep is em-
ployed, but the azimuth error of the signal is indicated by the
horizontal coordinate and the elevation error as the vertical.
Azimuth error
15-52
ELECTRO-OPTICAL DEVICES
Inverse range Indicated
by length of "wings0
Down
Left
Right
Type G
Sometimes called a "spot with wings" display. Similar to
type F, with spot extended to a line whose length is inversely
proportional to range to the target. Used mainly for gun-laying,
the correct direction and range being indicated when the signal
just fits between the two short vertical reference lines.
TypeH
Known also as the "double dot" display, indicating range,
bearing, and elevation- A modified type B display, in which
alternate range sweeps are displaced slightly horizontally, thus
producing two "dots" from a single echo. The position of the
left dot is that which would be indicated by the type B display.
The right dot is displaced vertically by an amount such that the
angle 9 is roughly proportional to the elevation of the target.
left-*
Right
Typel
An intensity-modulated radar display, sometimes called a
"broken circle" display, used with a conical scanning antenna.
Each echo is represented by an arc of a circle whose radius rep-
resents range, and for which the shortness of the arc indicates
the error in pointing at the target. Thus the arc A represents
a target far to the left and below, while .# is a target just a little
above and to the right. A target dead ahead would be repre-
sented by a complete circle.
CATHODE-RAY-TUBE DISPLAYS
15-53
Synchronizing 0
-
Slgnal
TypeJ
Essentially a type A display bent into a circle. Useful for
accurate time or range measurement when a continuously run-
ning (crystal or other) oscillator can be used. The circular
trace is obtained by applying two sinusoids from the same source
to the two pairs of deflection plates, one sinusoid being 90° out
of phase with the other. The synchronizing pulse which occurs
at 0° also initiates the phenomenon to be observed, and the time
to be measured, for example the range of a radar echo or the
delay in a network is obtained from the angular position of the
observed signal. The radial deflection is obtained by applying
the signal voltage to a central electrode of the CRT (type 3DP1).
The sweep may be delayed so that zero time occurs at 0° on
some previous rotation of the sweep.
TypeK
A radar display used with systems sending out two beams in
slightly different directions. The type A sweeps from the two
lobes are displaced slightly horizontally. By adjusting the
angular position of the transmitting antennas until the signal
height of the two corresponding displaced signals is the same,
bearing or elevation information as well as range may be ob-
tained.
TypeL
Sometimes called * 'back-to^ack' ' A displays. Used with two-
lobe radar systems, the signal S would indicate a target to the
left. Changing the direction of the antennas until the opposite
signals are of equal strength gives bearing or elevation of target
as well as range.
15-54
ELECTRO-OPTICAL DEVICES
Range
TypeM
A modification of the basic type A display, in which a cali-
brated variable delayed "step" voltage is applied to one of the
vertical deflection plates, in order to give more accurate range
information. In practice, the step is shifted along the display
until the signal to be ranged comes just at the edge of the step.
Type 1ST
Combines features of types K and M in order to give more
accurate range and bearing or elevation information.
Range
Type O
Sometimes designated as a "type A with a notch" display.
Useful for accurate ranging on an echo. The horizontal sweep
speed is increased for a short time interval, the beginning of the
interval being adjustable and accurately calibrated. The signal
under observation is placed in the center of this expanded por-
tion of the sweep, whereupon the reading of the delay dial gives
the range directly.
Range
CATHODE-RAT-TUBE DISPLAYS
15-55
Type P or PPI
The most widely used intensity-modulated radar display,
called plan position indication (PPI), in which the range of the
echo is given by its distance from the center of the display, and
its bearing by the angular position. The display may be either
stabilized, so that north is at 0°, or unstabilized, in which case
0° represents the ship's or plane's heading. To produce this
display, a radial sweep starting from the center at the instant of
the transmitted pulse moves outward in the direction in which
the antenna is pointing at the moment. The rotating sweep
may be produced by a linear sawtooth current in a single-asis
deflection coil mounted around the neck of a magnetic deflection
CRT, the coil being rotated in synchronism with the antenna.
Alternatively, a stationary two-axis coil may be used, with x-
and 2/-axis sawtooth currents whose amplitudes are at any
given time proportional to cos S and to sin 6 respectively,
6 being the direction in which the antenna is pointing. Electro-
static deflection CRT may also be used, sawtooth voltages
similarly modulated being applied to the two pairs of deflection
plates.
Two modifications of the centered PPI are: (a) the "open-
center PPI," in which increased accuracy in determining azi-
muth at close ranges can be obtained by starting the radial
sweeps from a circle of arbitrary radius, and (b) the "delayed
PPI," in which increased accuracy in determining the range of
distant objects results from delaying the beginning of each
sweep from the center by an arbitrary known time.
Off-center PPI or Sector Display
The off-center PPI is a variation of the centered PPI described
above, in which the center of the pattern may be arbitrarily
displaced in any direction, and the sweep expanded, so that any
desired portion of the entire area within the range of the radar
set can be made to fill the entire screen of the CRT. Such a
display affords the possibility of greatly increased resolution
while still preserving the undistorted map feature of the PPI.
This is accomplished in the case of a rotating coil PPI by the
superposition of a steady deflecting field upon the rotating sweep
field. In the fixed x- and 2/-axis coil system, the same result may
be attained by proper control of the delay and sweep speeds of
the two components. The resulting display is often called a
"sector display," although it may not be a complete sector if
the origin of the pattern is not on the CRT screen.
15-56
ELECTRO-OPTICAL DEVICES
TypeR
The designation R (for range) applies to a type A display in
which a fast linear sweep is employed, the start of the sweep
being delayed by a precision calibrated delay circuit. Precision
electronic time markers may also be used. The R display is
generally used hi conjunction with a standard type A display in
which the time interval covered by the R sweep is indicated on
the A sweep by intensifying the corresponding time interval.
Both sweeps may be displayed on a single CRT at the same
time by using electronic switching of the two sweeps and vertical
displacement of the two traces.
Range
Type RHI
This display is used to indicate the range and height of air-
craft, hence the symbol RHI, Since the vertical distance
(height) to be measured is in this case usually much less than
the horizontal distance (range), the useful area of the CRT face
can be greatly increased by expanding the vertical dimension.
The display is usually obtained by applying simultaneous saw-
tooth currents to the x- and y-deflection coils of the CRT, such
that ix = A cos 8-t and iy = nA sin d-t, where 0 is the angle of
elevation of the antenna, and n is the vertical expansion factor,
usually between 5 and 10. In practice, the range sweep is
usually simplified to ix — A-t, the resulting distortion being
unimportant. Lines of constant height are straight and hori-
zontal. The range sweep may be delayed for increased range
resolution at large distances.
SECTION 16
SOUND-REPRODUCTION SYSTEMS
AUDIO FACILITIES FOR SOUND SYSTEMS
j^^ BY HOWARD A. CHXNN PAGE
1. Sound Studios 02
2. Microphones 04
3. Audio Amplifiers and Control Equipment 06
4. Monitoring Facilities 09
ELECTROACOUST1C EQUIPMENT
BY R. J. KOWALSKI
5. Auditorium Acoustics 11
6. Loudspeakers 13
7. Amplifiers and Control Equipment 14
PUBLIC-ADDRESS SYSTEMS
BY R. J. KOWALSKI
8. Indoor Sound-reinforcing Systems 15
9. Outdoor Sound-reinforcing Systems. ... 15
10. Paging Systems 16
SOUND RECORDING AND PROJECTION
ART. PAGE
11. Recording Practices, by O. B. GUNBY. . . 19
12. Projection Practices, by J, D. PHYFB. , . 21
RADIO TELEPHONE BROADCASTING
BY HOWARD A. CHTNN
13. Program Distribution Systems 27
14. Program Lines 27
15. Broadcasting Transmitter Plant , . 28
16. Broadcast Frequency Allocation , . 30
17. Broadcasting Station Service 32
18. Fidelity Requirements of Broadcast
System 33
POLICE RADIO
BY H. F. MICEEL
19. Frequencies 36
20. Power and Range 37
21. Equipment , 37
16-01
SOUND-REPRODUCTION SYSTEMS
Sound energy Is transformed into some other form and retransformed back into sound
for one of three general purposes: it may be desired to reproduce the sound instantly but
at some other location, as in telephony or broadcasting; it may be desired to reproduce the
sound at some subsequent time, as in phonographs and sound pictures; or it may be de-
sired to reproduce the sound instantly and at the same location, but with increased energy
content, as in public-address systems. The discussion herein is limited to reproduction by
electric means, or at least partially by electric means, although other means are some-
times used (e.g., acoustic phonographs).
An electrical sound-reproduction system consists always of a microphone, or device to
translate sound energy into electric energy; an amplifier and associated control equipment,
to control the loudness of the sound; and a loudspeaker, or device to translate electric
energy into sound energy. Similar considerations govern the choice and installation of
these devices in all systems.
In addition, in phonographs and sound pictures there are devices to record the sound
permanently and to effect the subsequent reproduction of the sound, as well as means to
synchronize the recording and reproducing machines accurately. In telephone and radio
broadcast systems a transmission link is inserted in the circuit; also in telephony a com-
plicated switching system is included to permit any subscriber to talk privately to any
other subscriber. (See Section 17).
AUDIO FACILITIES FOR SOUND SYSTEMS
By Howard A. Chinn
1. SOUND STUDIOS
Sound-reproduction systems in common use employ a single channel for transmission
and for reproduction. Regardless of how many microphones are utilized for a given pick-
up, their outputs are ultimately blended into one audio channel. This results in a single-
channel system which imposes problems of a special nature upon the design of studios and
sets used for sound broadcasting or for sound recording.
When a person listens to sound directly, the listening is done with both ears, or bin-
aurally. Binaural hearing is indispensable for the localization of sound and for sound
perspective. When listening to music in a-eoncert hall, for example, one can largely ignore
disturbing noises, provided they originate in a direction that is different from that of the
desired sound and are not of unreasonable intensity. Furthermore, it is even possible to
concentrate upon a particular section of the orchestra (for example, the strings in pref-
erence to the brass, or vice versa) and to ignore sounds that may be of no interest, or per-
haps even unpleasant.
In listening to a single-channel system, on the other hand, nearly all sense of location of
the sound is lost, as well as its extension in space. (A simple but effective demonstration
of this is to block one ear, while conversing in a noisy room. The ability to continue to
understand the speaker will be greatly impaired, if not entirely destroyed, because of the
inability to exclude unwanted sound.) This same limitation exists when sound is trans-
mitted over a single channel and reproduced by a loudspeaker system. Even though both
ears are used for listening to the loudspeaker, the sound comes from a single source (multi-
ple-unit loudspeakers, such as are sometimes required on wide-range, high-fidelity systems,
do not change the effect) and the ability to discriminate against undesirable sounds is
almost completely lacking. Hence, the sound that is heard from radio or television broad-
casting, and in the cinema theater, is lacking in sound perspective. The design of studios
for sound-reproduction purposes must be undertaken with these considerations in mind.
By combining acoustically correct architecture with suitable microphone pick-up and
blending techniques, a single-channel sound system will produce pleasing results. How-
ever, the acoustical design problems are considerably more severe than those encountered
in ordinary architectural work. Since the ability to localize sound is lacking, it is necessary
to remove all sources of confusion or interference incident to monaural listening. This
16-02
SOUND STUDIOS
16-03
may be done by (a) proper control of reverberation, (&) the elimination of echoes, and (c)
the elimination of disturbing noise. The first two items involve problems in acoustical
treatment; the last one, problems of sound isolation — the two are not necessarily related.
OPTIMUM REVERBERATION TIME. Experience has shown that the most satis-
factory reverberation time for broadcasting or sound-recording studios is less than that
which is considered optimum for binaural listening. (See Section 12.) However, the
reduction should be no more than is required to obtain the desired result. An excessive
reduction in reverberation time will result in the elimination of the reverberant char-
acteristics normally associated with the type of sound being reproduced. For example,
the timbre or quality of a church organ being played in an acoustically dead room would
sound as if it were out-of-doors. The reverberant quality associated with church music
would be completely missing. The proper amount of reverberation must, therefore, be
retained to create the desired psychological effect.
The use of studios that are acoustically too dead results in another undesirable effect.
Musical organizations performing in an environment of this type are handicapped in
several ways. The performer, discovering that his instrument does not produce the sound
intensity to which he is accustomed, generally tries to produce the normal amount of
sound, with the result that he concludes the studio is a "difficult" one in which to work.
In addition, the performer may find that it requires special attention to hear the other
members of his group in order to keep in time and in tune. Finally, the listener gains the
impression that the orchestra is a much smaller aggregation than it actually is.
The type of the production dictates the optimum reverberation time for any given
studio. In general, studios intended for speech or dramatic productions are less rever-
berant than those used for musical presentations. It is evident, therefore, that no one
optimum will cover all situations. Furthermore, since maximum studio usage requires
that a given unit be capable of accommodating all types of productions, some means of
adjusting the acoustics is not only desirable but actually essential for full Bexifaility. In
Fig. 1 there are shown recommended minimum and maximum reverberation times, at
2.0
to
g 1.8
§'••
K2
1.0
2 0.6
UJ
£ 0.4
UJ
(5 0.2
<e
I 1 I
. SOUND STUDIO REVERBERATION TIME
RECOMMENDED RANGE AT IOOO CPS
(AS A FUNCTION OF STUDIO VOLUME)
5 10 20
STUDIO VOLUME -THOUSANDS OF CUBIC FEET
FIG. 1. Recommended Range of Sound Studio Reverberation Time (at 1000 Cycles)
too
1000 cycles, as a function of studio volume. The most reverberant condition shown is suit-
able for symphonic orchestras, church organ music, and other musical productions nor-
mally associated with large halls; the least reverberant condition is suitable for dramatic
productions and musical programs where no '"room tone" is desired.
It is desirable that studios be designed to provide a variation of reverberation time be-
tween the two limits shown in Fig. 1. This amount of flexibility makes it possible to adapt a
studio for praeticaDy any kind of production. The advantages of being able to do this are
obvious. The maximum load factor for every unit i& assured without placing groups in
studios having unsuitable acoustical characteristics. This feature alone will justify many
times over the additional design problems that variable acoustics entails. Since a studio
with variable acoustics can be used for all types of productions, fewer studio units are
needed in any given group. The results are not only greater performer satisfaction but
also a smaller initial investment and a smaller operating cost for the studio group as a
whole.
16-04 SOUND-REPRODUCTION SYSTEMS
VARIATION OF REVERBERATION TIME WITH FREQUENCY. In addition to the
reverberation time at a specific mid-range frequency, the manner in which the rever-
beration time varies with frequency is important. Various investigators have discussed
the shape of the reverberation characteristic from theoretical, subjective, experience, and
environment viewpoints. Their findings are not conclusive, however. Furthermore,
practically all were based upon binaural listening conditions.
Experience gained from broadcasting and recording studio applications seems to in-
dicate that, except in the larger studios (i.e., those of about 50,000 cu ft or more) the
reverberation time should be essentially independent of frequency (in practice, however,
the humidity often limits the reverberation time at high frequencies) . In the very large
studios some increase in the reverberation time at the low frequencies is often beneficial
for the type of productions for which such studios are used.
In a studio having variable acoustics, provisions may also be made to obtain variations
in the shape of the reverberation-frequency characteristic. By properly locating various
types of acoustical material on the absorbing side of adjustable panels (or on the wall back
of movable panels) , it is possible to change the shape of the characteristic, within limits.
Variation, at the low frequencies, from a fiat characteristic to a rising or falling one may
often prove useful. A change of 20-30 per cent above a flat characteristic at 100 cycles
to a like amount below should prove entirely adequate.
SOUND DECAY RATE. The manner in which sound decays in a studio is as important
as the reverberation time, or even of greater importance. In some studios, sound does
not decay logarithmically as geometrical acoustics assumes. Experience indicates, how-
ever, that a smooth logarithmic decay of sound results in the most acceptable type of stu-
dio. A decay curve of this nature insures the absence of discrete echoes and eliminates
one of the sources of confusion to monaural listening already mentioned. For good
acoustics it is generally considered desirable to have a constant decay rate for at least the
first 30 or 40 db.
The desired type of sound decay can be obtained by creating a diffuse distribution of
the sound. This can be done in a number of ways, such as employing a random distribu-
tion of the sound-absorbing materials, by the use otf serrated walls and ceilings, or by sub-
stituting curvilinear surfaces for flat ones. It can be shown, theoretically, that curved
panels, as contrasted to fiat serrated panels, increase the area over which sound wave is
dispersed. Likewise, it follows, that multicurved surfaces are an improvement over
cylindrical ones. However, it is not yet generally realized that from a sound pickup view-
point the diffusion of sound in an enclosure can be carried too far. Experience indicates
that an entirely adequate amount of sound diffusion can be readily obtained with serrated
flat surfaces. Consequently, there is little need to resort to the more complicated (from
a construction viewpoint) curvilinear surfaces, except as may be deemed desirable from
an esthetic point of view.
ACOUSTICAL NOISE LEVELS. The residual noise in studios, from all sources,
should be as low as possible. However, there is a lower limit below which it is not justi-
fiable to reduce the noise from either a theoretical or economical viewpoint. The max-
imum, sound intensities normally encountered in studios at the normal microphone pick-
up position (relatively close to the speaker for speech but relatively distant for music)
range from about 75 db (above the acoustical reference level of 10 ~~16 watt per cm2) for
speech to 95 db for music. The listener, on the other hand, indicates that noises that are
50 to 60 db below the signal are either unobjectionable or not detectable. Taking these
considerations into account, together with the economic ones, it is evident that a residual-
noise level 25 db above the reference level is quite satisfactory. Sound isolation methods
are discussed in detail in Section 12.
BIBLIOGRAPHY
Morse, P. M., and R. H. Bolt, Sound Waves in Rooms, Rffo. Modern Physics, April 1944, p. 69. (In-
cludes an excellent bibliography.)
Articles in the Journal of the Acoustical Society of America, Journal of the Society of Motion Picture
Engineers.
2. MICROPHONES
The types of microphones most commonly employed for program pick-up purposes are:
condenser, moving-coil (or dynamic), velocity-actuated ribbon, crystal (piezoelectric),
and combination units. These last microphones usually combine a velocity- and a pressure-
acttiated ribbon or velocity-actuated ribbon and a moving coil into a single unit. The
phasing between the two units of the assembly is arranged so as to obtain a directional ef-
MICROPHONES 16-05
feet, such as a unidirectional or a cardioid pattern. The characteristics of various micro-
phones are discussed in detail in Section 13.
The output level of wide-range, high-quality microphones is extremely low— so low, in
fact, that the signal-to-thermal-noise ratio existing at the output terminals of the micro-
phone often determines the overall performance of the system. The sound intensities
existing at the microphone position for the usual type of program productions is such that
a net insertion gain of 50 to 60 db is usually required to raise the output level to 0 VUT the
standard reference level (see below). Still greater gain is required, of course, to raise the
level sufficiently for transmission over program circuits, for operating loudspeakers and
recorders, or for modulating a transmitter.
The output impedance of condenser and crystal microphones is very high, and, as a
rule, these units are operated directly into the grid of a tube. On the other hand, the out-
put impedance of the moving-coil, ribbon, and combination microphones has ranged from
a few ohms to several thousand ohms, depending upon the type. Such a variation greatly
restricted the universal use of various kinds of microphones with different equipment.
The situation has now been recognized, and microphones intended for broadcasting pur-
poses have been standardized at 150 ohms. In most cases, a transformer must be supplied
as an integral part of the microphone in order to provide the standard output impedance.
MICROPHONE PLACEMENT. In determining the proper placement of a micro-
phone for a given type of program it is necessary to take into consideration the directional
properties of the particular microphone being used as regards both its amplitude and its
frequency response characteristics. Each type of microphone has a directional character-
istic peculiar to that type, and both the horizontal and the vertical plane directional pat-
tern of the microphone must be considered in connection with its application and place-
ment. Some microphones are unidirectional, others bidirectional, and still others non-
directional in the horizontal plane. These properties are extremely important and useful
for discriminating against undesired sources of sound and for obtaining a desired relation
between sounds from different sources.
Figure 2 illustrates the placement of two bidirectional microphones which, for the pur-
poses of illustration, are assumed to have a figure S directional pattern in the horizontal
plane. The performance being
picked up is assumed to consist of
a chorus, a soloist, and an accom-
panying orchestra. Microphone
A is used for the chorus and soloist
pick-up, the artists being grouped
on both sides of the instrument.
The orientation of this microphone
is such that the null point or direc-
tion of minimum pick-up is towards
the orchestra. Microphone A,
therefore, is actuated primarily by
the chorus and soloist and picks up
very little of the orchestra music.
Microphone B, on the other hand,
is so located as to derive its major p^ 2 An r^t^tion of the Placement of Bidirectional
source of energy from the orches- Microphones to Achieve Control of Sound Pickup
tra, and its null point is towards the
singers. The electrical outputs of these microphones, one of which consists primarily of
the voices and the other of the musical accompaniment, are then properly combined or
"mixed" so as to obtain the desired balance. The technician responsible for this operation
has control over the relative magnitudes of the singers' voices and the music. He can
adjust the relation between the two and also the overall amplitude to obtain any desired
result. Still other microphones may be used for picking up sound effects, announcements,
audience or crowd noise, etc. By the proper placement each microphone can more or less
be confined to the pick-up of its assigned source of sound.
Microphones having relatively sharp directional characteristics are sometimes used for
outdoor or long-distance sound pick-ups. These devices are particularly good for con-
fining the source of pick-up of sounds at a large outdoor gathering to a particularly in-
teresting part of the crowd such as a cheering section or a band of musicians. In tele-
vision pick-ups they provide a means for keeping the microphone otit of the camera angfe.
The use of more than one microphone for the pick-up of a given performer or group of
performers working as a unit (orchestra, chorus, etc.) is generally to be avoided. Serious
frequency and delay distortion is likely to result if more than one instrument is employed
for the pick-up because under these circumstances each microphone will be a different
16-06
SOUND-REPRODUCTION SYSTEMS
distance away from a given source of sound. As a result the sound waves do not reach
each microphone at the same instant, and the combined outputs of the microphones will
result in complete or partial reinforcement or cancelation, depending upon the resultant
phase relationships. Furthermore, the phase relation is dependent upon the frequency of
the sound source and does not, therefore, remain a constant quantity for all sounds.
In practice it is sometimes advisable, however, to countenance these potential sources
of distortion and use more than one microphone for the pick-up of a given group of per-
formers. For example, an orchestra may have a string choir too small for good balance.
Under such circumstances, supplementing the main microphone by a strategically placed
and judiciously used secondary7 microphone may enhance the overall balance. It is impor-
tant to note, in an operation of this type, that the contribution of the additional micro-
phones must always be maintained at a low level.
The frequency-response characteristic of some microphones varies with the angle of
incidence of the sound wave upon the instrument. Microphones that exhibit this char-
acteristic usually have a decreasing response to the higher frequencies as the source of
sound moves around from the front to the side of the instrument. In placing such micro-
phones this characteristic must be taken into consideration. The unidirectional dynamic
and the condenser microphones are of this type. The velocity, non-directional dynamic,
and crystal microphones, on the other hand, maintain the same relation between the high
and low frequencies at all angles of incidence.
BIBLIOGRAPHY
Hopper, F. L., Characteristics of Modern Microphones for Sound Recording, J. Soc. Motion Picture
Eng., September 1939, p. 278.
Marshall, II. N., and W. R. Harry, A Cardioid Directional Microphone, J. Soc. Motion Picture Eng.,
September 1939, p. 254.
Marshall, R. N., and F. F. Romanow, A Non-directional Microphone, Bell Sys. Tech. J., July 1936,
p. 405.
Olson, H. F., Elements of Acoustical Engineering. Van Nostrand (1940).
Olson, H. F., The Ribbon Microphone, Proc. I.R.E., May 1933, p. 655.
ADDITIONAL
PROGRAM
SOURCES
3. AUDIO AMPLIFIERS AND CONTROL EQUIPMENT
A complete sound system entails, in addition to microphones for converting sound en-
ergy into electrical energy, facilities for: (a) amplifying the exceedingly low microphone
output to a usable level; (6) blending, into a balanced whole, program elements from
several channels (known
as "mixing") ; (c) adjust-
ing the balanced program
to the desired transmis-
sion level without altering
TO OUTGOING the balance; (d) aurally
LINE and visually monitoring
the transmission.
These elements are
found in audio systems
used for broadcasting,
sound recording, and
public-address applica-
LEGEND tions. Figure 3 illustrates,
in block diagram form, a
typical audio system in-
corporating the elements
listed above. The com-
ponents of the complete
system are described below
in the order in which they
appear in the Hock diagram.
PRELIMINARY AMPLIFIERS. It is common practice in reproduction systems to
have a mixer volume control associated with each microphone or other source of pick-up.
As already noted, however, the output level of microphones is so low that any attenuation,
prior to amplification of the signal, would degrade the signal-to-noise ratio of the system
(the cause of the noise at this point being largely thermal). Therefore, before any volume
coiatroling ean be done, it is necessary to raise the level of the signal well above the ther-
Aa
AM
AP
As
LS
FIG. 3.
BOOSTER AMPLIFIER
MICROPHONE PRE-AMPLJFIER
PROGRAM AMPLIFIER
MONITOR AMPLIFIER
LOUDSPEAKER
M
MG
P
vc
VI
MICROPHONE
MASTER GAIN CONTROL
ATTENUATION PAD
MIXER GAIN CONTROL
VOLUME INDICATOR
Simplified Block Diagram of Typical Sound System Studio
Audio Facilities
AUDIO AMPLIFIERS AND CONTROL EQUIPMENT 16-07
mal-noise level. In fact, one of the cardinal principles of good audio system design is
never to permit the signal level to fall below the value existing at the output terminals of
the microphone. It is therefore common practice to insert a preliminary amplifier be-
tween the microphone and the mixer volume control (or any other circuit element such as
a sound-effects filter, dialogue equalizer, etc.). By using this arrangement the mixer con-
trol is introduced into a circuit at a point where the level of the microphone output has
been raised considerably above the thermal-noise level of the circuit. As a result, when
attenuation is introduced for mixing purposes, the signal-to-noise ratio is not degraded.
Preliminary amplifiers usually consist of one or two stages of amplification having an
overall gain in the neighborhood of 30 to 40 db. The amplifier must be carefully designed
because any noise originating in it will be amplified by the following amplifier stages. It
is therefore imperative that amplifier noises such as microphonics and hum background
be practically non-existent in the preliminary amplifier. The input transformer of the
preamplifier, if one is used, is a particularly susceptible point for the pick-up of stray,
unwanted, interfering fields. This unit must be very carefully shielded both electro-
statically and electromagnetically.
Low-impedance microphones, such as the dynamic and velocity types, are connected
to the input of the first amplifier tube by means of a suitable transformer. However,
microphones of this type are basically voltage-generating devices; consequently their
output impedance (150 ohms in broadcasting practice) is not matched to the input im-
pedance of the preliminary amplifier. Rather, the preliminary amplifier is designed to
have a high input impedance, thereby realizing as much of the open-circuit voltage of the
microphone as possible. The input transformer is normally designed with as high a step-
up ratio as commensurable with the required response-frequency characteristic. The
leads connecting the microphone to the preamplifier input transformer may be several
hundred feet long without seriously impairing the performance of the device.
The condenser and crystal types of microphones are connected directly to the input of
the amplifier tube through a suitable network of resistors and condensers. In this case
it is desirable that the leads connecting the pick-up device to the amplifier tube be of very
low electrostatic capacitance. (Connecting cable capacitance attenuates the micro-
phone's output voltage but does not impair its response as a function of frequency.) It
is common practice to make these leads very short by building the preamplifier into the
mounting which houses the microphone head. In the floor-stand type of mounting this
amplifier is sometimes built into the base of the stand.
In the design of preliminary amplifiers care must be exercised that the output stage has
adequate power-handling capacity. Since no gain control is ever inserted between the
microphone and the preliminary amplifier, the input to the amplifier will vary over wide
limits. The output level of the usual microphone under the average conditions met in
practice has already been noted. However, if a microphone is placed close to a musical
instrument that is being played very loudly (or near another source of loud sound) its out-
put level may be as much as 20 db higher than that "normally" obtained. The output
stage of preliminary amplifiers must be capable of handling without overloading the out-
put level resulting from this input level. The output of the preamplifier is usually matched
to the mixer circuit impedance by means of a suitable output transformer. For broad-
casting applications the standard output impedances are 600 and 150 ohms.
MIXER VOLUME COHTROLS. A mixer circuit is an arrangement of volume controls
for combining into one program channel, in any desired proportions, program elements of
several channels. The multiple microphoneT transition, and fading effects, which con-
tribute so much to program continuity, are obtained with mixer controls. For instance,
separate microphones may be used for a soloist and for the accompanying orchestra (Fig.
2) and the outputs combined to form a balanced whole. Since the gain of each micro-
phone channel may be regulated independently of the others, a method of controlling the
balance between various pick-ups is provided which does not impair the quality of the
individual sources of sound.
A mixer is also used to "fade down" a musical transmission so that announcements or
talks may be superimposed. All these effects contribute a degree of smoothness to a
program which would otherwise be impossible. Because of their use these controls are
sometimes known as "faders."
The mixer control is, in effect, a variable-resistance attenuation pad, usually of a T
structure, having a constant or nearly constant input and output impedance. The de-
vice is capable of providing attenuation over a range from 0 to about 120 db. The at-
tenuation generally varies uniformly with the angle of rotation of the control knob through-
out the range from 0 to approximately 50 db. From this point to maximum attenuation
the increase is very rapid, occurring in perhaps one-tenth of the full arc of rotation. For
broadcasting applications the standard miser control impedances are 600 or 150 ohms.
16-08
SOUND-REPRODUCTION SYSTEMS
MIXER MATCHING NETWORK. A mixer matching network combines the output
of a number of mixer controls into a single channel while maintaining correct impedance
relations. The matching network provides the proper load impedance for the individual
mixer controls and also the desired source impedance for the following circuit element.
FIG. 4a. Differential Matching Network Having Like Input and Output Impedance
One of the simplest forms of matching networks is shown in Fig. 4<z. In the general
case of n mixer positions, the value of the building-out resistors, Ri, is
R(n - 1)
Where the input and output impedance of the network are assumed to be alike and equal
to R.
The loss between the output of any given mixer control and the matching network load is
db loss
FIG. 46. Minimum-loss Differential Matching Network. Input and output impedances are not alike-
If the requirements of like input and output impedance are waived, a lower loss network
can be used, Fig. 46. Here, the building resistor value R% is
R(n - 1)
j%i> —
n
The output impedance RQ is
_ R(2n - 1)
RQ = 5
The loss of the network is
db loss = 10 logio (2n - 1)
In, tfcJs case the output impedance can be restored to the same value as the input im-
pedance (or to any other value) by means of a matching transformer.
MONITORING FACILITIES 16-09
BOOSTER AMPLIFIER. The amount of attenuation introduced in an audio system
by the mixer controls and the associated matching network is often so great that ampli-
fication must be supplied before further volume controlling (see Master Volume Control,
next paragraph) can be effected. The amplifier used for this purpose is termed a booster
amplifier. It usually employs one or two stages of amplification, has a gain of 30 to 40
db, and is designed to operate from a source impedance and into a load impedance of
finite value (e.g., 600 and 150 ohms in broadcast service).
Whether a booster amplifier is required between the mixer circuit and the master gain
control is determined by the signal levels existing for normal input levels and normal set-
tings of the controls. Its use is indicated if, by its omission, the signal would fall below
the level existing at the output terminals of the microphone.
MASTER VOLUME CONTROL. The master volume control or "gain" control is
"master" over the output of the individual mixer controls. After these mixer controls
are adjusted to obtain the proper relation between the various parts of the performance
the resultant overall volume of the program material may be adjusted to the desired level
by means of the master gain control without affecting the balance that exists. This de-
vice also ^permits the properly balanced performance to be faded in or out while the same
relation is maintained between the individual parts of the program. The master gain
control is similar in construction and operation to the mixer volume controls.
PROGRAM AMPLIFIER. The purpose of the program amplifier is to bring the level
of the studio output up to the point necessary to permit its being fed directly into the audio
amplifier stage of a transmitter, into the program line connecting the studio with a trans-
mitter, into a loudspeaker amplifier or a recording system. At a network key station,
the output of the program amplifier is fed into a bus for distribution to the proper network
or networks.
This amplifier follows the preamplifiers, mixers, and master gam control to amplify the
output of the microphones or other program source further. Although one preamplifier
is needed for each microphone in use, only one program amplifier is necessary for a given
studio channel. The amplification obtainable in these units is generally in the vicinity of
50-60 db. The amplifiers are usually capable of an output level of approximately 250 milli-
watts without serious overloading. The input impedance of this amplifier is matched to
the output impedance of the preceding master gain control by means of a suitable trans-
former. The output impedance is similarly matched to the load which follows this unit.
BIBLIOGRAPHY
Chinn, H. A., Broadcast Studio Audio Frequency System Design, Proc. I.R.E., February 1939, p. 83.
Chinn, H. A., CBS Studio Control-Console and Control-room Design, Proc. I.R.E., May 1946, p. 287.
Monroe, R. B., and Palmquist, C. A.. Modern Design Features of CBS Studio Audio Facilities, Pr&c.
IJ2.J2., June 1948, p. 778.
4. MONITORING FACILITIES
AURAL MONITORING FACILITIES. A monitoring system consisting of a suitable
amplifier and loudspeaker is a part of every complete sound system. These facilities pro-
vide a means for those responsible for the production of hearing the program exactly as
it is being sent to the transmitter, the network, or the recorder. It is essential that the
fidelity of the aural monitoring equipment be in keeping with the remainder of the broad-
casting or recording system.
An output of 10 to 25 watts and an amplification of approximately 50 db are generally
obtainable from the monitoring amplifier. The input impedance of the monitoring
amplifier is usually very high in order that it may be bridged across the program circuit at
a convenient point without affecting the level or impedance balance of the circuit to any
appreciable extent. The output circuit is provided with a suitable transformer to effect
an impedance match with the particular type of loudspeaker or speakers being em-
ployed.
Broadcasting and sound-recording control rooms often afford a limited amount of space
for the installation of a monitoring loudspeaker, placing several special requirements upon
the design of the unit. For instance, the directional properties of the loudspeaker must
be such as to provide uniform coverage for all occupants of the control room who are con-
cerned with the production in hand. This requirement usually entails some special ar-
rangement to injure uniform distribution of the high frequencies. Furthermore, since
the loudspeaker may be relatively close to the listener, multichannel loudspeakers (if
used) must be especially arranged so that the separate sources of sound cannot be dis-
tinguished as such.
18-10 SOUND-REPRODUCTION SYSTEMS
VOLUME INDICATOR FOR VISUAL MONITORING. A volume indicator is used
in order to provide a precise, visual means of determining the volume level of the program
material being transmitted by an audio system. The standard volume indicator consists
of a copper oxide rectifier and a d-c indicating instrument. The characteristics of the
rectifier, together with the dynamic, electrical, and other performance characteristics of
the indicating instrument, are all carefully standardized. When calibrated and used in
the prescribed way, the standard volume indicator gives an accurate indication of volume
level. This is expressed as so many "vu" above (or below) reference volume — the number
of vu being numerically equal to the number of decibels that the volume level is above (or
below) reference volume.
REFERENCE VOLUME — VU. Reference volume is that level of program which
causes the standard volume indicator, when calibrated and used in the prescribed way,
to read 0 vu. By definition, the reading of the standard volume indicator shall be 0 vu
when it is connected to a 600-ohm resistance in which there is flowing 1 milliwatt of sine-
wave power or n vu when the calibrating power is n decibels above one milliwatt.
Reference volume, as applied to program material, should not be confused with the
single-frequency power used to calibrate the volume indicator. Speech or program waves
that result in a volume reading of 0 vu have instantaneous peaks of power many times 1
milliwatt and an average power which is a fraction of 1 milliwatt. In other words, ref-
erence volume is not 1 milliwatt, except in the special case of sine-wave measurements.
DBM VS. VU. For steady-state measurements a reading in "vu" denotes a specific
single-frequency audio power; for dynamic program indications vu denotes only a 'Vol-
ume" level. This dual meaning of vu is avoided by use of the term "dbm" for all steady-
state measurements. Using this terminology, a reading expressed in dbm indicates the
power level of a steady single-frequency signal where the number of dbm is equal to the num-
ber of decibels above (or below) a reference power of 1 milliwatt. On the other hand, a
reading in vu denotes a volume-level indication of a program signal. A vu reading can
be made only on a standard volume indicator (since the dynamic characteristics are in-
volved) whereas sine-wave power level measured with the standard volume indicator or
with any other suitable a-c instrument can be expressed in dbm.
The practice of expressing measurement-signal levels in dbm, and of limiting vu to ex-
pression of dynamic volume levels, has certain advantages. Thus, dbm is a unit of finite
audio power, whereas vu may be considered only a unit of volume level and, as mentioned
above, has no connotation of finite power level.
However, it is necessary to establish a relation between the vu level to be used for pro-
gram peaking and the dbm level to be used for performance measurements. It has been
found that on typical program peaks reaching a given crest amplitude the standard volume
indicator reaches an indication 8 to 14 db below that reached on a steady tone of the same
crest amplitude. To take into account this 8- to 14-db difference in response, it is standard
practice to require that performance requirements be met at a single-frequency test-tone
level 10 db higher than the normal program level. This will reasonably insure that sys-
tem performance is within standards under most operating conditions.
TALK-BACK EQUIPMENT. A "talk-back" system is generally employed in order to
provide a means for communication between the control room and the studio during the
course of rehearsals. This equipment consists of a microphone in the control room, a
suitable amplifier, and a loudspeaker in the studio. By means of this equipment the
technician or the production man in the control room may talk to and direct the per-
formers in the studio during rehearsals.
The talk-back equipment is interlocked with the regular studio equipment so that the
studio microphones and the control-room monitor speaker are turned off whenever the
talk-back equipment is energized for use. This prevents the generation of an acoustic
feedback because of coupling between the input and the output circuits of the amplifier
systems. The regular preamplifiers, studio channel amplifier, and monitor amplifier as-
sociated with the studio are sometimes employed, by suitable switching means, for the
talk-back service. Inasmuch as both services do not function simultaneously, this ar-
rangement results in an economical use of the equipment already available. The switch-
ing complications, however, often do not justify this practice. Under these circumstances
separate or partly separate talk-back equipment is used.
BIBLIOGRAPHY
CHnn, H. A., D. K. Gannett, R. M. Morris, The New Standard Volume Indicator and Reference
Level, Proc. J.S.B., Jan. lf 1940; also Bell Sys. Tech. J., Jan. 1, 1940.
Chinn, H. A., DBM vs. VU, Audio Engineering, March 1948, p. 28.
AUDITORIUM ACOUSTICS
16-11
ELECTROACOUSTIC EQUIPMENT
By R. J. KowalsM
5. AUDITORIUM ACOUSTICS
When an auditorium is designed for use with a sound-reproducing system one of the
most important design considerations is the acoustic characteristics. (See also Section
12). The sound emanating from the stage loudspeakers reaches the listener only after
being influenced by the acoustic conditions of the auditorium. In view of the technical
perfection of modern sound-reproducing equipment, it is frequently these acoustic con-
ditions that determine whether the sound reaches the ear of the listener with all its original
naturalness and realism or whether it is distorted, unnatural, and wholly unsatisfactory
to the listener.
The most common acoustic defects encountered in auditoriums are reverberation, echo,
resonance, poor distribution (loud and dead spots), and noise.
Optimum reverberation times for auditoriums of various sises are shown in Fig. 1. It
will be noted that as the volume increases the allowable reverberation time also increases.
Optimum Reverberation Period for Sound
Motion Picture Theatres at 512 Cycles
3000
10,000 100,000
Volume !a Cxi Ft
FIG. 1. Optimum Reverberation Times for Auditoriums
1,000,000
It will also be noted that the optimum reverberation time recommended is from 10 to 20
per cent below the usual values for an auditorium that uses live talent without a sound-
reinforcing system. This is because there is an abundance of sound energy and hence
reverberation is not necessary to augment loudness. In fact, some recent thinking favors
overtreating an auditorium with sound-absorptive material to eliminate most acoustic
defects and then artificially introducing the proper amount of reverberation in the sound-
reinforcing system, by means of reverberation or echo chambers. These can be designed
to give any desired amount of reverberation and can be quickly and cheaply changed to
meet different conditions.
It will be noted in Fig. 2 that at the lower frequencies longer reverberation periods can
be tolerated while at the higher frequencies the allowable period is somewhat reduced.
o ISO
CM
If
c 120
>
o 60
1 40
0 3
I
1
s
1
1
111
1
1
s
s
Optimum Reverberation- Frequency Characteristic
In Per Cent of Reverberation 71n>e et 512 CPS
^
>s
^
-^
]
•^
•«>
*•«
-«i.
i !
1
i
"p
*^4
i
i ;x
i
N
'
i
i
0 100 1000 10,000
Frequency In CPS
FIG. 2. Optimum Reverberation Time with Frequency
By referring to the table of absorption coefficients of building materials in Section 12 it
will be noted that most materials have a different coefficient for different frequencies.
Because of this, it is possible by proper selection of materials to arrive at a design which
will give optimum reverberation time throughout the frequency range. Owing to the
extension of the low-frequency and the high-frequency ranges of modern reproducing
equipment great care should be observed in the choice of sound-absorbing materials and
treatment.
16-12 SOUND-REPRODUCTION SYSTEMS
Echo consists of a delayed repetition, sometimes several rapid repetitions, of the original
sound. It is most often encountered in large auditoriums, particularly those with curved
ceilings and walls and other surfaces sufficiently remote from the source of original sound
to cause a definite time interval between the arrival of the original and reflected sounds at
the listener's position. A multiple or nutter echo (several distinct repetitions) is often
caused by parallel walls with smooth hard surfaces. With the extension of the high-
frequency range of modern equipment the problem of echo and sound concentration was
somewhat intensified because the high frequencies, or high-pitched notes, on account of
their short wavelengths, are more easily reflected by small, smooth surfaces.
Echoes have much the same effect as reverberation in that they tend to blur speech and
music. Echoes are eliminated by first localizing them and then applying light drapes or
other sound-absorbing materials, or by breaking up the regularity of the offending sur-
faces by stepping, angling, etc., thereby dispersing or scattering the sound striking them.
When it is necessary to add sound-absorbing material to correct for reverberation time, it
is best to apply it first to the rear wall of the auditorium. Since the speakers are directed
toward this wall it is usually the worst offender for echoes. If the side walls are parallel,
the next best place to apply treatment material is on alternate panels of the side walls
with the treated panels staggered so that no two untreated surfaces are opposite each
other. This helps to eliminate flutter echo between walls. Flutter echo between ceiling
and floor can best be avoided by specifying heavy carpeting with padding in the aisles and
heavily upholstered seats.
The phenomenon of resonance, or the ability to vibrate best at certain frequencies, may
occur either in structures or in the air in rooms. The effect is a build-up or overemphasis
of certain frequencies. Structural resonance usually is not harmful unless the resonant
body is mechanically coupled close to the source of sound. An offending object can usually
be located quickly by connecting an audio-frequency oscillator to the input of the sound-
reproducing system and varying the frequency until resonance is reached. By surveying
the room while this frequency is maintained, the vibrating object can usually be located.
The vibration, can then be eliminated by changing the mounting or adding damping ma-
terial. Resonance in air chambers is usually encountered in small, highly reverberant
rooms; it rarely is a problem in the main body of a large auditorium, though it may give
trouble in smaller sections such as the stage, which usually has hard, bare, parallel walls,
or under a balcony, in alcoves, or in foyers. To eliminate such resonance conditions on
the stage, as well as to help reduce reverberation on the stage, absorbing material should
be draped in the region around the loudspeakers.
Poor distribution of sound (i.e., loud and dead spots due to the shape of the auditorium)
can usually be overcome by the proper type and proper orientation of the loudspeakers.
This problem is discussed further in article 6.
Noise may be defined as any unwanted sound. Noise is undesirable particularly because
it has a masking and a frequency discriminating effect on the desirable sounds which,
therefore, require added loudness or power to override the noise An auditorium in a noisy
city location should have its outside walls insulated against the transmission of outside
noises into the auditorium. See Section 12 for a full discussion of noise reduction.
The following recommendations will serve as a guide in designing an auditorium to get
the best results from a modern sound-reproducing system:
1. All seats should be of the heavily upholstered type.
2. Heavily padded carpeting should be used in all aisles and corridors.
3. The rear wall, being potentially the greatest source of echo, should be lined with an
efficient type of sound-absorbing material and/or sloped or otherwise shaped to direct the
reflected sound to nearby audience or treated areas to prevent echo.
4. Surfaces with concave curvature should be avoided as much as possible. If such
surfaces are necessary they should be broken up with smaller convex flutes to disperse the
sound or heavily treated to absorb most of the incident sound.
5. Large unbroken surface areas, except when used for beneficial reflections, such as
reflection from the splayed ceiling and walls at the proscenium, should be avoided.
6. Long narrow auditoriums, high ceilings, and excessively long and low balcony over-
hangs should be avoided.
7. The cubical content of the auditorium should be made as small as possible, compat-
ible with the seating capacity and architectural design.
8. A rising slope in the orchestra floor should be used to give unobstructed "sound'1
lines as well as "sight" lines.
9. All auditorium walls should provide sufficient sound insulation to prevent extraneous
noises from entering.
10. All machinery and ventilating noises should be isolated from the auditorium.
LOUDSPEAKERS 16-13
POWER REQUIREMENTS. In calculating the power requirements for a sound-
reproducing system there are several factors to be taken into consideration. IB an out-
door installation the listener gets only the direct sound from the speakers, while in a small
room or auditorium the total energy- reaching the listener is the sum of the direct energy
and the reflected reverberant energy. Hence the total absorption of the auditorium must
be known to determine the acoustic power required. It is also necessary to know what
sound pressures it is desired to attain before calculating acoustic power. For high-
fidelity reproduction of both sound and music it is generally assumed that sound pressures
on peaks and loud passages will reach 20 dynes per sq cm, or 100 db above the threshold
of audibility. Finally, since we are chiefly interested in the electrical power needed in the
reproducing amplifiers, it is necessary to consider the conversion efficiency of the loud-
speakers and the coverage efficiency, that is, the percentage of the total radiated sound
energy actually distributed to the required area.
In making calculations for any given installation, the following formula is recom-
mended:
where Sy = floor or seating area in square feet.
EL = loudspeaker efficiency expressed in fractions thus, 50 per cent — 0.50.
AQ = average absorption coefficient of room.
ST — total area of room surfaces in square feet.
RF — reflection coefficient of seating area. This equals 1 minus the absorption co-
efi&eient RF = (1 — AF).
The constant in this formula is calculated to give a sound pressure of 100 db. If less
acoustic power is required, as in small rooms, the power as calculated by the formula may
be decreased an equivalent number of decibels. For outdoor reproduction, the absorption
is considered infinite, hence the factor in brackets goes to unity, simplifying the equation
to P = O.OOOQSjp/^L. Assuming an efficiency of 45 per cent, which is average for a mod-
ern directional loudspeaker of the type used in outdoor installations, the formula becomes
P = 0.002$ F. This indicates that, in order to develop sound pressures of 100 db without
the benefit of reverberation, using a loudspeaker with an overall efficiency of 45 per cent,
it is necessary to supply 2 watts of electrical energy for each 1000 sq ft of audience area.
6. LOUDSPEAKERS
Through the years, a good many different types of loudspeakers have been developed
to convert electrical energy into acoustic energy (see Section 13). Among them were the
head-phone-type magnetic-diaphragm units, the condenser speakers, the magnetic-arma-
ture speakers, and the moving-coil-type speakers. In recent years the moving ooil or so-
called dyiiarnie speakers have proved the most efficient, and hence this is the only type
now in common use. The magnetic field that the voice coil moves in is supplied by a field
coil energized with direct current or by a permanent magnet. With the new magnetic
alloys like Alnico it is possible to get flux densities in the permanent-magnet type that are
as great as those obtained when using an electrically energized field. Hence the efficiencies
of the two types are comparable. The permanent-magnet type is rapidly becoming the
most popular, because, though it is a little more expensive to build, it saves the cost of an
electrical field supply as well as considerable additional wiring, which is quite a factor when
a good many speaker units are located at remote points. Aside from the type of field,
dynamic speakers are classified in two general types: (1) the direct radiator type and <2)
the horn type. The direct radiator type uses a large cone with a relatively snail-diameter
voice coil for a radiator. This unit is generally mounted on a flat baffle or in a cabinet.
The horn-type unit has a relatively small diaphragm driven by a large-diameter coil. This
unit is specifically designed to be used with a directional type of horn.
The direct radiator or cone type of speaker on a flat baffle is generally used in small
spaces such as hotel guest rooms, school classrooms, or hospital ward rooms. Although
this type of loudspeaker is frequently considered non-directional, it has a definite distri-
bution angle, particularly at the higher audio frequencies. For a rough approximation
at the most important frequency range, this angle may be considered to be 90°, that is,
45° off from either side of the central axis. Since the shape of the cone is symmetrical,
this distribution angle is the same for both the horizontal and vertical planes. In de-
termining the number of speaker units to place in a given room, not only the power-
handling capacity but also the coverage must be considered. A floor plan of the room
may be sketched to scale, and speakers may be located, and the coverage of each plotted.
16-14 SOUND-REPRODUCTION SYSTEMS
If the distribution angle of one speaker does not cover at least 75 per cent of the total area,
two or more speakers should be placed along the wall until this much of the area is covered.
All speakers must be connected to operate in phase. When speakers of this type are used
for incidental music such as in a hospital or restaurant it is preferable to increase the num-
ber of speakers and hence cut down the power per speaker to get the most uniform sound
intensity throughout the room.
For larger installations in auditoriums or in unconventionally shaped rooms much more
efficient distribution of sound energy can be obtained through the use of horn-type loud-
speakers with directional horns. The more concentrated beam distributes the sound in
the desired area and at the same time keeps it off walls and ceilings, hence helping to
avoid serious echo effects. In de luxe installations where high-fidelity reproduction of
music is desired best performance can be obtained by using a two-way speaker system with
multicellular exponential high-frequency horns and a folded baffle for the low-frequency
speakers.
In auditoriums or theaters, the location of the speakers for best illusion is usually above
and to the front of the proscenium arch. If this location will not allow for the projection
of sound into the rear of the orchestra floor under the balcony, it will be necessary to place
additional speakers to the sides of the proscenium directed to cover this area. These
speakers should be kept as high as possible and should be angled to get as little sound as
possible into the front rows of seats. When locating speakers, caution should be used to
see that the projected sound beam does not pass through the microphone pick-up area
where it would cause acoustic feedback and hence limit the gain of the reinforcing
system.
When more than a single speaker unit is used, it is essential that all units operate in
phase. On better speakers, the phasing is carefully controlled in production and the
terminals of the speaker are marked so it is only necessary to connect all similar terminals
together to get proper phasing. If the speakers are not marked it is possible to energize
the speaker fields and then apply a small d-c voltage to each voice coil. By reversing the
polarity of the battery it is possible to determine to which terminal of the speaker the pos-
itive terminal of the battery should be connected to give a forward deflection of the speaker
diaphragm. If these positive terminals are connected all the speakers will be properly
phased.
7. AMPLIFIERS AND CONTROL EQUIPMENT
Before selecting the proper amplifier for a given installation it is necessary to determine
the power requirements as described in article 5. Strict adherence to this formula in small
auditoriums might indicate relatively low power requirements; however, the Research
Council of the Academy of Motion Picture Arts and Sciences recommends a minimum of
10 watts of audio power for the smallest of theaters. Though the average power used in
normal reproduction will be considerably below this figure, the reserve power will make
it possible to reproduce peaks and loud passages without distortion. This minimum of
10 watts is recommended for auditoriums up to 500 seats. The recommended power rises
approximately 10 watts for each additional 500 seats. In multiroomed installations like
hotels, the total power requirements are found by adding up the power requirements of
the individual rooms. Systems of this type frequently have a varying use factor for each
room so that all rooms might not have to be supplied simultaneously. Although this
use factor varies widely with different types of installations, the suggested values for hotels
are: 100 per cent for a single channel installation, 90 per cent for two channels, 75 per cent
for three channels, and 60 per cent for four channels.
For theatrical use the amplifiers should be capable of reproducing all frequencies within
the range of 50 cycles to 10,000 cycles.
PUBLIC-ADDRESS SYSTEMS
By R. J. Kowalski
Public-address systems fall in two general classifications according to application. A
system for amplifying speech or music presented directly to a large audience, whether in
an auditorium or out in the open, is appropriately named a sound-reinforcing system. A
system by which a speaker at a central location addresses people simultaneously at various
locations is known as a paging system. In general, the equipment specifications for sound
reinforcing, particularly indoors, are more exacting than those for paging applications.
OUTDOOR SOUND-REINFORCING SYSTEMS 16-15
8. INDOOR SOUND-REmFORCMG SYSTEMS
The essential requirements of a sound-reinforcing system are that it must pick up all
desired sounds and project them, unaltered, with sufficient intensity and distribution to
all listeners within a given area. For maximum effectiveness, the system should function
so as not to detract the attention of the listeners from the performers.'
When installing a reinforcing system in an auditorium, particular attention should be
given to the acoustic conditions. A certain amount of the sound energy emanating from
the loudspeakers finds its way back to the microphone. Unless the difference between
the level of the sound energy leaving the speakers and that arriving at the microphone is
greater than the gain of the system amplifier, the system will oscillate because of acoustic
feedback. Directional microphones aid in avoiding feedback, because, with them, it is
possible to position the axis of maximum response toward the desired sound and i;he null
axis toward the reflected sound. Mounting the microphones in acoustically treated com-
partments in the footlight trough also shields them from considerable reflected sound.
Unless feedback can be corrected by repositioning the microphones or redirecting the
loudspeakers it will be necessary to limit the gain of the amplifier and hence the amount
of reinforcing obtained. However, if the auditorium is well designed acoustically, there
should be no difficulty in getting sufficient amplification before feedback occurs.
The sound-reinforcing equipment in large auditoriums and theaters is usually custom
built and permanently installed. The microphones and preamplifiers are broadcast
quality, and the main amplifiers and loudspeakers are generally of the type used in sound-
motion-picture reproduction. The amplifiers should have uniform frequency response
over the complete range of audio frequencies from 50 to 10,000 cycles. The amplifier
output capacity should be such that at least 1 acoustic watt per 1000 ft of floor space can
be delivered. The amplifier should be able to deliver this amount of power with less tfaaa
2 per cent total harmonic distortion over the range from 50 cycles to 5000 cycles. The
loudspeaker system should have directional horns to distribute the sound energy efficiently
in the proper area. Many theaters employ two-way speaker systems for their reinforcing
systems as well as for the movie-sound system. The two-way system assures uniform,
highly efficient operation over the complete audio spectrum. The input equipment should
be highly flexible to accommodate a wide variety of microphone combinations because dif-
ferent types of programs require different pick-up arrangements. See article 2. Where
the pick-up area is great, such as an entire stage area for vaudeville and stage productions,
microphones are usually located in the footlight troughs, suspended from the scenery
drops, and sometimes concealed in stage props. The optimum spacing of footlight micro-
phones has been found to be 8 to 10 feet. In order to control the input from all these
microphones to get the proper balance in sound levels, a mixer is required with controls
for each input. The most satisfactory location of the mixer console is somewhere in the
audience area, preferably at the head of the balcony where the operator can hear the
direct sound from the system speakers and adjust the various inputs for best balance.
An excellent example of a high-quality sound-reinforcing system is the one at Radio
City Music Hall, New York City. Because of the width of the stage, a three-channel re-
inforcing system is used to obtain the best possible illusion. The stage microphones are
split into three groups: right stage, center stage, and left stage. Each group is fed through
its separate section of the mixer console, then to its separate amplifier, and thence to the
speakers over the proscenium arch. The speakers, too, are split into three groups which are
fed by the three amplifier channels. Therefore, a sound originating on the right side of tiie
stage is picked up by the right-side microphones, amplified by the right channel amplifier,
and reproduced by the right group of loudspeakers. As an actor moves across the stage the
sound moves with him, creating an excellent illusion. Sound reproduction in this system
is so well balanced that, despite the tremendous size of the auditorium, the people in the
remotest corners can hear as well as those seated up front.
Besides these large, expensive systems, many small portable systems are available
commercially that can be used for meetings, banquets, etc., in small rooms. These sys-
tems generally contain microphones, folding microphone stands, amplifier, and loud-
speakers all in one compact carrying case. The sides of the case serve as baffles for the
speakers when they are put in use.
9. OUTDOOR SOTJND-REINFORCING SYSTEMS
Sound-reinforcing systems for outdoor use are generally higher powered than indoor
systems, because the average area to be covered is greater, and the power per unit area is
16-16 SOUND-REPRODUCTION SYSTEMS
also greater since there is no beneficial reverberation to augment the direct sound. In
order to utilize the available sound energy most efficiently, highly directional loudspeaker
horns are used almost exclusively for outdoor work. Since the low-frequency cutoff on
practical sized horns of this type is well up in the audio-frequency range, the system
fidelity is not generally as good as that found in indoor systems. The fidelity could be
improved with a more expensive speaker set-up; but, in most cases, intelligibility is more
important in outdoor systems than fidelity. Since the low-frequency tones do not con-
tribute materially to intelligibility, they may be sacrificed in the interest of holding down
the practical size of the equipment. As in indoor systems, the loudspeakers should be
located to give the best illusion; but they should be carefully directed to prevent any
direct energy from reaching the microphone and causing feedback. This problem is ob-
viously much less serious in outdoor than in indoor installations.
For indoor work, the ribbon-type velocity microphone is the most popular because of
its uniform frequency response, its useful directional pattern, and its ability to pick up
sounds at a considerable distance. In outdoor work this microphone is not too satis-
factory because it is somewhat fragile and is subject to extraneous noises generated by the
wind disturbing the ribbon. A much better microphone for this application is the dy-
namic pressure type.
10. PAGING SYSTEMS
Although the sound-reinforcing application of public-address equipment is probably
more familiar to the layman, paging systems have become even more important. During
the war years, large permanently installed plant broadcast systems became vital parts of
most big factories, making it possible to locate key men quickly in the acres of floor area,
and to coordinate production activities throughout the plant. Announce systems of
many types, installed on practically all fighting ships of the fleet, proved to be the most
important means of internal communication. New-type announcing systems for schools
make it possible to communicate quickly with all rooms and to distribute educational pro-
grams as desired. Besides these, there are hundreds of more commonplace applications
like train announcers at railroad stations and call systems in hospitals, hotels, restaurants,
and other business establishments.
PLANT BROADCAST SYSTEMS. Though the leading manufacturers are building
equipment components specifically designed for industrial use, there is no such thing as a
universal industrial sound system. The desired services, plant layout, and conditions of
operation vary so greatly that each installation becomes a custom-engineered job. Some
of the many services furnished by a properly designed and managed industrial system
are:
1. Paging. The telephone operator or a special paging operator, through announce-
ments to selected areas of the plant, can quickly locate personnel.
2. Emergency and alarm. By using combinations of special signal generators and
verbal announcements the system is highly effective in fire, damage, and accident control.
3. Time signals, The system may be connected to the main time clock to broadcast
time signals at preselected intervals.
4. General announcements. The paging operator or one of the plant executives may
use the system to supplant the bulletin boards for messages pertaining to plant operations.
5. Work music. To increase the efficiency of personnel, planned music programs may
be given at periodic intervals during the work period. The source of the music may be
recordings, a wired-in service, or radio programs.
6. Entertainment. During rest or lunch periods, programs may be presented by live
talent, such as employee groups or visiting celebrities.
7. Morale building. The system may be used to bring about more personal contact
in personnel relationship through inspirational messages, drives, safety campaigns, and
announcements of general interest.
In recent years many scientific tests have been made on the value of music in industry.
These have proved that periodic musical intervals have a beneficial effect on most types of
workers, but especially on those engaged in repetitive manual operations associated with
modern assembly-line manufacture. The chief effects are the relief of fatigue and bore-
dom and the dispelling of nervous tension. Tangible results have been accomplished in
the reduction of labor turnover, reduction of accidents, increased production, and im-
proved quality of product.
The central control equipment of the average plant broadcasting system is located in a
sound-treated room that serves as a studio. The central control console, or mixer, is
located here to control the various inputs. These inputs may include a paging microphone,
one or more studio microphones, one or more executive microphones in the executive
PAGING SYSTEMS 16-17
offices, one or more radio inputs, one or two phonograph turntables, time clock signal
generator, and possibly a fire or other emergency alarm signal generator. The mixer
console should include an attenuator to control each input and a master attenuator to
control the overall level of any combination of inputs. It should also include a volume-
indicator meter to permit the operator to maintain the proper signal level on the system.
The output of the mixer is fed into a program amplifier which in turn feeds a group of zone
selector switches on the operator's console. In almost any setup it is best to divide the
plant into convenient zones or areas for programming and paging. In a simple system the
division might merely be "offices" and "factory," but in a larger plant an individual zone
might be established for each building or each 'department. This makes possible selective
announcements or paging calls to any one part of the plant. The output of the zone
switches is fed to the individual zone power amplifiers that drive the loudspeakers in each
.zone. If the plant is small and all zones are in a single building, h is best to install all the
zone power amplifiers in the studio or equipment room so that they will be in a central loca-
tion to facilitate service work. However, if the plant is spread over considerable area, or
in many buildings, it is best to mount the zone power amplifiers in the buildings they
serve. The input signal can be fed from the studio at the sone power amplifier at zero
level over standard telephone lines which normally link most buildings of a large plant.
This is more economical on amplifier power than trying to feed high-level energy over long
lines.
In a larger system it might be desirable to have provisions for sending two different
programs to different areas simultaneously. This is especially helpful when an urgent
paging announcement has to be sent to one zone during a regular musical program. The
particular zone can be paged on a separate channel without disturbing the music going
out to the other zones. To do this, it is necessary to add a second program amplifier and
another volume indicator meter to monitor the level on this second channel. Each input
switch should be a three-position switch so that, besides an "off* portion, any of the in-
puts may be connected to either of the two program amplifiers. The soae selector switches
should also be three-position switches so any zone may be connected to either of the two
program channels or may be completely disconnected. In plants subject to serious
emergencies, the switching arrangement may be so arranged that, whenever the alarm
signal generator is sounded, it takes priority over all other inputs and is automatically
fed to all loudspeakers regardless of the position of the zone switches. Alarm contactors
to energize the signal generators may be located throughout the plant at critical points.
Associated with the studio equipment should be a monitor speaker with a switch which
enables the system operator to monitor audibly any program going out to the plant or fco
check on proper tuning of the radio receiver before connecting it to the program bus.
Adjacent to the studio should be a suitable storage room for storing the record library for
musical programs as well as spare microphones, etc., for the system. Records for in-
industrial use should be selected with some care. In general popular records are suitable
for factory working periods with possibly light classical music for the plant restaurant
during the lunch hour. Considerable research has been done on the psychological effects
•of different types of music. By reference to the bibliography foEowing this article, ad-
ditional information on this subject may be obtained. From a practical standpoint,
since most factories are rather noisy the recorded music selected should have fairly co®r-
stant level. If a recording having very loud and very soft passages is reproduced in a
noisy area, the low passages will be lost completely unless the overall level is made so high
that the loud passages are annoying.
The primary design consideration for equipment for industrial use is roggedneas. In
many cases the equipment will have to operate continuously through a 24-hour working
day. All components should be conservatively rated so they are used well witfein their
capacity and hence will give long life. Precautions should be taken in the design ol the
^switching system so that the equipment cannot be damaged by improper operation of the
controls. Occasionally inexperienced personnel will attempt to operate the equipment,
,and so these safeguards are necessary.
The necessary overall fidelity of the equipment varies with the application and tlie
noise levels encountered. If the system is to be used solely for verbal annoumoeiaeiita,
an overall frequency response of 300 to 3000 cycles is adequate; however, if music is to be
reproduced, the response should extend from 50 to 10,000 cycles. This wide freqiaeacy
range is not merely to give high-fidelity reproduction but also to add needed definition to
music being reproduced under adverse conditions. Noise generally occurs at specific
frequencies. If the music is reproduced with a limited band of frequencies, some of the
frequencies will coincide with those of the noise and hence will be masked. The loss ol
certain notes reduces the definition of the music and makes it hard to follow. ^ Of course,
.the difficulty can be overcome by making the volume louder to override the noise, but this
16-18 SOUND-REPRODUCTION SYSTEMS
might make the music annoying. By extending the frequency range, the definition may
be improved without increasing the overall volume.
Plant noise levels and the shape of the building determine the size, type, number, and
locations of loudspeakers. In high-noise areas, best results are obtained from horn-type
loudspeakers which can direct the sound energy to the important areas. However, if the
noise level is below 90 db, well-baffled cone-type loudspeakers should be used. It is pos-
sible to get more uniform distribution over wide areas with this type of speaker. The
power required for any given zone may be computed fairly accurately by means of the
formula given in article 5. Where the existing noise level is above 100 db, the power as
computed by the formula should be increased accordingly. Most standard types of
microphones are suitable for reproduction from a studio ; but if the microphone is located
in a high-noise-level area out in the plant, a specially designed close-talking microphone
should be used to reduce the response to unwanted room noise. A phonograph turntable
for industrial use should be weighted and dynamically balanced, and it should be driven
by a heavy-duty motor to insure constant speed. Home-type record changers should
never be used in an application such as this.
Before actually selecting the equipment for a particular plant, a thorough plant survey
should be made. This survey should supply the following information :
1. Noise. AH sources of noise should be located on a copy of the plant's floor plans as
well as the average level of the noise in all areas. This information can be quickly ob-
tained with a portable sound-level meter.
2. Coverage. On the basis of the above measurements, the types of speakers should
be selected and their locations marked on the print.
3. Plant zoning. All areas should be zoned with reference to industrial operations for
determining switching requirements.
4. Locations. The location of the studio, input sources, amplifier equipment, and con-
trols should be determined and marked on the prints.
5. Special considerations. Any special information such as desired priority of signals
and temporary microphone locations should be noted.
On the basis of the above information it will be possible to engineer a system that will
exactly fill the needs of the plant. To fill the needs of a wide variety of different plants,
some manufacturers have designed a series of very flexible sectionalized units which may
be put together like building blocks to make up any desired type of system out of standard
equipment.
NAVY ANNOUNCE EQUIPMENT. A modern fighting ship is a complex organization
with a huge staff of personnel engaged in a wide variety of activities necessary to operate
it. To coordinate all these activities it is necessary to use a shipwide, selective, announce
system. When the ship is under way, the orders originate on the bridge; when the ship
is in port, the ship's control center is the quarter deck, hence orders originate from this
station. The ship is divided into sections so that orders may be issued to selected sec-
tions. In addition, each section is subdivided into smaller subgroups which can be sep-
arately disconnected in the event of battle damage; then if one speaker line is shorted,,
it may be cut loose so that it does not affect the rest of the system. Besides the shipwide
general announce system, a large ship has many more specialized systems such as: (1) the
engineer's announce system between the engineering log room and the various fire rooms,
boiler rooms, and other engineering spaces; (2) the damage control system between the
damage control office and several damage control stations; (3) turret control systems for
communication between the turret captain in each of the primary battery turrets and the
gun pointer, the gun layer, and the various shell-handling and power-handling decks below
the turret; and (4) the secondary battery announce system communicating between the
gun directors and the gun mounts of the secondary batteries. Moreover, there are high-
powered systems using a single loudspeaker that can be directed for ship-to-ship, ship-
to-dock, and ship-to-plane sound communication, and a variety of low-powered inter-
communication systems between specialized points.
The requirements for ruggedness in ship equipment are even more exacting than in
equipment for industrial uses. All ship equipment must be shockproof, and loudspeakers
on. the weather decks should be weatherproof, watertight, and blastproof to stand the
pounding seas and the terrific concussion of gunfire. Microphones are generally of the
close-talking dynamic type to reduce the response to undesired noises.
SCHOOL SYSTEMS. Small specialized versions of industrial systems have been.
designed for school use. The control console is located in the principal's office, where
announcements and programs originate. The control console has a selector switch for
each room so that announcements may go to any room or any group of rooms. A special
connection with a talk-back amplifier makes it possible to use each classroom speaker as
a microphone. In this way, it is possible to establish two-way communication between the
RECORDING PRACTICES
ie-i9
Available inputs besides microphones include a radio
principal and any of the teachers.
tuner and a record player.
in J^ f a^.fe*^es<>f school equipment should be simplicity of controls and relatively
low cost,_which is achieved by a slight sacrifice in overall quality of reproduction, while
maintaining a safety factor in the choice of component parts to insure dependability of
operation .
BIBLIOGRAPHY
Biims-MeyerH. Music iir Industiy, Meckamcal Bngineerins, January 1943.
PublSheS" aS^^ Programming Music in Industry, AW1 Soc. Compaq Ao^ocs, and
Halpin, 0 D., Industrial Music and Morale, /. Actwiticat Sec. Am.
Music in. Industry, Industrial Recreation Assodatkai (1944)
belvm, Ben, Programming Music for Industry, J. Acoustical Soc. Am.* October 1943,
SOUND RECORDING AND PROJECTION
11. RECORDING PRACTICES
By O. B. Guuby
Sound motion pictures are released extensivery, either 16 mm or 35 mrn, depending upon
the application. The use of 16-mm film is on the increase in advertising and educational
fields. The majority of the studios make all their pictures oa 35-rnm film, even though
some of them will be reduced to 16 mm before release, because of the greater fiexibiliiy
obtainable from the 35-mm equipment commercially available.
Recent trends in the design and operation of sound-motion-picture equipment include
the general use of electronic mixers (volume compressors) or limiters to wsary the volume
range of the recordings or to prevent overloads on loud signals Also, particularly in the
recording of music, synchronously driven acetate recordings are often made so that an
immediate playback of the recorded material is possible, thus permitting a quick and ac-
curate check on quality.
A block diagram of a typical production-type dialogue channel is shown in Fig. 1. The
same type of a channel may be used for recording sound effects or for the recording of
SOUND STAGE
RECORDER ROOM
FIG. 1. Simplified Scoring or Dialogue Recording Cfaannel
music, which is usually referred to as scoring. For scoring, however, it is customary to
use more microphone inputs than are indicated for a dialogue channel. Since the picture
is usually made before the music is recorded, a motion-picture screen is generally provided
on a scoring stage so that the orchestra leader can watch the picture while he is directing
the orchestra,
16-20
SOUND-BEPRODUCTION SYSTEMS
In a dialogue channel the microphones are usually located 4 ft or less away from the
actors, but out of range of the camera. The microphones are usually mounted on long
adjustable booms so that they can be moved to follow the action closely and yet avoid the
camera. Microphones of the unidirectional type are used frequently because of their
ability to discriminate between the wanted sound from the set and the extraneous noises
from other directions.
The sound stage in which the recording channel is used must be constructed to exclude
external noises. This frequently involves double wall construction with intervening air
spaces and accoustic treatment on the interior to provide the desired reverberation time.
The mixer is located near the set in a position where the operator has an unobstructed
view of the action being recorded. This helps him to anticipate changes in mixer adjust-
ment to suit the sound source. Monitoring is accomplished with high-fidelity headphones.
The remainder of the recording channel may be located in a small room on the sound
stage, in a recording truck parked adjacent to the stage, or in a centrally located building
on the studio grounds and connected to the sound stage by suitable transmission lines.
Figure 2 is a block diagram of a typical rerecording channel. It is essential that the
console be installed in a room having acoustic properties comparable to those of an average
-DIALOGUE CHANNEL
FILM LL_4MPT| M«XEI» UBOOSTHRU VARIABLE |_j«"|
PHONO. [-jPBE.AMP.fl pAp j-j AMp fl pAD {-j^l
FJt-M M I] COMPEN-LJ BOOSTER M M
[ PHONO. |-[PRE-AMP.[-| gATOR [-[ AHP. f| ,
FILM Up,
PHONO. np
RERECORD1NQ REVIEW ROOM
RECORDER EQUIPMENT ROOM
FIG. 2. Simplified Rerecording Channel
theater so that the desired sound quality may be determined through the monitor speaker
system, as the numerous sources are blended together to make a final sound track.
The various sound sources are usually recorded on separate films in order to provide
the desired degree of flexibility. In general, the sound tracks will include dialogue, music,
and any number of sound-effect tracks that may be required. These films are threaded
in separate film phonographs whose audio outputs are individually controlled by the
operator at the mixer console. The threading of the films is indicated by suitable marks
so that sound and picture are synchronized. The various film-handling machines are
driven by Selsyn motors which provide an electrical interlock during the operating
cycle.
During a rehearsal the film phonographs and the projector are run by the Selsyn driving
system, and the operator varies the audio signals from the film phonographs to fit the mood
of the picture. Several rehearsals are usually required in obtaining the desired effect.
Once this has been achieved, the films are rethreaded and another run is made, including
the film recording machine. During this run the operator endeavors to repeat the changes
in level, etc., that were made during the successful rehearsal. The procedure is repeated,
if necessary, until a satisfactory rerecording is made.
During the rerecording process, in addition to changes in level that are made in the
incoming signals, changes may also be made in the frequency response to adjust for day-
to-day differences in the original recording or to obtain certain special effects such as tele-
phone quality, old phonograph quality, and so forth.
PROJECTION PRACTICES
16-21
The more progressive studios usually have facilities for the con* ~>I of reverberation.
A reverberation chamber is one means of control. A portion of thx and requiring re-
verberation is fed into a loudspeaker in the chamber; the sound is picked up by a micro-
phone located in the same room and mixed with the original sound to obtain the desired
effect.
A third type of recording channel, the single-film system, is shown in Fig. 3. This
channel is generally used in the field for the original recording of newsreels and to a lesser
extent for recordings on locations impractical for recording with the more cumbersome
production-type channels. As the
name implies, tH« system uses one
film on which both the picture is
photographed and the sound is re-
corded.
The more modern equipments
use a specially designed camera
having in it a mechanically filtered
drum on which the light beam from
a compact recording optical system
can be focused. With some equip-
ments, a conventional camera is
used and the sound is recorded
directly on the camera sprocket.
The amplifier is designed to have
small size, light weight, and low
power drain, and the facilities pro-
vided are kept to a minimum.
Power for the amplifier, exposure
lamp, and camera motor are often
provided by a single small low- FlG> 3 Sn^ Fdm R^jrf^ Channel
voltage storage battery.
Some newsreel channels use class B pushpull recording since this type of track provides
excellent noise reduction by optical means and does not add to the size, weight, or power
dram of the equipment. This track requires rerecording to standard track before it can
be released to theaters, but since it is always rerecorded to provide sound effects, music,
etc., this requirement presents no problem in the production of the newsreels.
Modern recording equipments are capable of producing films having a fiat frequency
response over a range greater than 30 to 10,000 cycles and a volume range in excess of 50
db. However, in practice it is usually found desirable to restrict the frequency range from
about 70 to 7000 cycles and the volume range to approximately 20 to 25 db. This limita-
tion in frequency and volume range is a compromise resulting from the necessity of evolving
a technique that provides commercially acceptable sound quality while recognising the
following variable factors: (a) reasonable quality tolerances for each of the steps in sound
motion picture production, (6) the wide variety of conditions under which sound films are
reproduced in the many theaters.
12, PROJECTION PRACTICES
By J. D. Phyfe
The sound-reproducing system of a modern motion-picture theater is the combined prod-
uct of many highly specialized arts and sciences, embracing the fields of optics, acoustics,
electronics, and mechanics.
The following description of the major component items of a typical sound-reproducing
system will illustrate how these components are combined into a complete system.
The equipment housed in the projection room usually consists of two picture projectors
and associated lamp houses, two soundheads which are mounted below the projector
mechanisms, and an amplifier system. The projectors and soundheads for all theaters
are quite similar, the power output rating of the amplifier and loudspeaker systems being
modified to compensate for changes in the seating capacities of various theaters.
The sound-reproducing industry has set progressively higher standards of performance,
as exemplified hi constant development work fostered by all manufacturers of theater
equipment. Tentative standards of reproduction have been established by the Research
Council of the Academy of Motion Picture Arts and Sciences.
The film, upon which are photographed both the picture and sound records, must be
moved through the mechanism of the soundhead at a constant rate of speed to insure a
16-22
SOUND-BEPKODTJCTION SYSTEMS
high quality of sound reproduction free from "wows" or "flutter/' These terms denote
minute variations in. the speed of the film.
Advances have been made in the design of the film-moving mechanism to reduce to a
minimum irregularities in speed of the film. Two types of film motion filter are in cur-
rent use, both employing a film-driven rotating drum coupled to a flywheel. One type,
OH Filrr
Outer Case
Sotfdly Connected
to Drum Shaft
Inner Flywheel
Free to Rotate on Shaft.
Driven by Oil Fiim Only,
FIG. 4. Soundhead Film Motion Filter (Rotary Stabilizer)
known as the Rotary Stabilizer (see Fig. 4), consists of two flywheels connected by a
viscous medium. The other type utilizes a solid flywheel in conjunction with a dampened
idler roller for its filtering action.
A picture of a modern soundhead is shown in Fig. 5. The view is of the "operating
side" of the unit through which the film passes.
Light from a source termed an "exciter lamp" passes through an optical system where
the dimensions of the beam are rigidly defined into a narrow slit 0.00125 in. wide and
0.084 in. long. This slit image is focused upon the sound track of the film, which is moving
FIG. 5. Operating Side of Modern Soundhead
and presenting a continuously variable ratio of clear film to the dark or exposed area of the
film that is being scanned by the light (Fig. 6). The film effectively serves to control the
transmission of the light in conformity with the light and dark areas that comprise the
souad record. The variation in the transmission of light is translated into & corresponding
variation in current by means of a photoelectric cell. (See Section 15, article 7.)
PROJECTION PRACTICES
16-23
Because the photocell currents are weak, it is necessary to provide a means of ampli-
fication; this may consist of a one- or two-stage voltage amplifier. Amplifiers are usually
separate units, either incorporated into the soundhead or mounted on the front wall of the
projection booth near the soundhead. They may also be placed in the main amplifier
rack and coupled to the soundhead by means of transformers or suitable low-capacity
coaxial cables.
Further amplification of the photocell voltage is furnished by the main or power ampli-
fier, raising the low-level currents to a satisfactory value where they can be made to operate
the theater loudspeaker system.
In order that the projectionist be informed constantly of both the volume level and
quality of the sound, a small monitor loudspeaker is installed in the projection room.
Pboto-ceU
•Scanning Beam of Ught
Sound Track
Direction
of
Him Travel
Photo-cell
/ Objective I
^ — Condensing Lets
FIG. 6. Optical System of Modern Soundhead
Equalizers are frequently employed to adjust the electrical response characteristics of the
amplifier system so as to provide optimum acoustical results in a given theater.
It is common practice to select the output of the desired soundhead by alternate switch-
ing of the exciter lamp currents or by selecting the audio output of either soundhe&d by
means of a "change-over switch" or '"fader."
The projectionist is notified of the proper time for making the change-over between
projection equipments by two small cue marks. These marks will appear in the picture
area of the film and are visible on the screen. The cues are placed several seconds apart
on the film as it passes through the outgoing projector. The first mark signals she oper-
ator to start the motor of the incoming machine. The second cue mark, appearing shortly
after the machine has attained full operating speed, marks the point of actual change-over.
The picture is switched by an electric dowser actuated by a foot switch operating in syn-
chronization with the sound change-over.
TWO-WAY LOUDSPEAKER SYSTEM. The loudspeakers employed in tbeater
sound reproduction are located behind the picture screen. Small perforations in the
screen, not noticeable from the seating area of the theater, permit the sound to pass readily
through the screen. A typical two-way loudspeaker system is shown in Fig. 7.
16-24
SOUND-BEPRODUCTION SYSTEMS
The wide frequency range and the large power-handling requirement of modern theater
loudspeaker systems cannot be met by a single speaker mechanism. The result has been
the development of the two-way loudspeaker in almost universal use today. For the
higher frequencies, a unit having a small light-weight diaphragm coupled to a multicellular
FIG. 7. Two-way Theater Loudspeaker System
directional horn is employed. The low-frequency portion of the signal is assigned to a
unit having a larger diaphragm coupled to a very large horn or baffle. The division of the
high- and low-frequency components is accomplished electrically through a "cross-over
network." The schematic diagram of such a network appears in Fig. 8. The cross-over
frequency is in the region of 400 cycles.
Crossover Network
. Hfgh-Frequenqy
Reproducers
_ Low-Frequency
Reproducers
FIG. 8. Schematic Diagram of Crossover Network for Two-way Loudspeaker System
A block schematic of a complete theater sound-reproducing system is shown in Fig. 9.
The relative circuit positions of the components covered above may be readily observed.
RECENT DEVELOPMENTS. Recent achievements in motion-picture-sound engineer-
ing are the development of the control-track system of reproduction and the drive-in type
of theater. The first-named system employs a control track consisting of variations in
the area of exposure of the small portion of film lying between adjacent sprocket holes.
RADIO TELEPHONE BROADCASTING
16-25
The system has been utilized to produce a 96-cycIe tone, the frequency being governed by
the number of sprocket holes per second passing a small scanning %ht. The variations
in light actuate a separate photoelectric cell as described earlier in this chapter. The
photocell current, after amplification, is rectified and used as a control voltage to regulate
the output level of the main theater amplifier and to cut into operation an auxiliary loud-
speaker system placed at each side of the picture screen. This complete system permits
a tremendous volume range not otherwise obtainable and provides a wider source of sound
SOUND
EXC. LAMP
SUPPLY
Hta»-nt£m*£i*e
SPEAKER
j-0— DO
SWITCH
EXC. LAMP
SUPPLY VOLTAGE
1
SOUNDHEAD
*
{
1
PHOTOCELL.
POLARIZlKa
VOLIAOE—
AUDIO:
PHOTOCELL
POLARIZING
VOLTA3E —
AUDIO
Hb-^HDO
SOUNDHEAD
2
-c
t
o
t SOUND
HANGE-OVER
SWITCH
* EXC. LAMP MONITOR
FIG. 9. Overall Block Diagram of Theater Sound-reproducing System
during loud passages than speakers alone placed behind the screen; it heightens the dra-
matic effect of certain loud passages,
DRIVE-IN THEATERS. The popularity of the drive-in type of theater has Increased
considerably during the last few years. The picture is shown on a large outdoor screen.
The patrons remain seated in then- automobiles, which are located in an arc to permit
viewing the picture through the windows. The trend is toward the use of individual
loudspeakers which may be placed inside the cars.
BIBLIOGRAPHY
Kimball, H. R., Applications of Electrical Networks, J. Soc. Motion Pictwre Engineers, Vol. 31 (October
1938).
Levinson, Nat., and L. T. Goldsmith, Vitasound, J". Soc. Motion Picture Engineers, VoL 36 (August
1941).
Reiskind, H. I.f Reproducing Systems, J. Soc. Motion Picture Engineers, VoL 36 (August 1941).
RADIO TELEPHONE BROADCASTING
By Howard A. Chima
Radio broadcasting is a means for delivering intelligence for general reception at distant
points. A complete system consists of: (a) a radio broadcasting transmitting system;
(b) the medium through which transmission takes place; (c) a number of receiving in-
stallations.
A radio broadcasting transmitting system consists, essentially, of:
1. A studio, stage, theater, auditorium, or other suitable place for the performance that
is to be broadcast. (See article 1, above.)
2. An acoustoelectric device (microphone) actuated by sound energy and delivering
electrical energy. (See article 2, above.)
3. Amplifiers for increasing the amplitude of this electrical energy. (See article 3
above.)
4. Control equipment for the regulation and adjustment of this electrical energy. (See
articles 3 and 4 above.)
5. Wire lines to carry the electrical replica of the original sound waves from the studio
to the radio transmitter.
6. Radio transmitter for converting this electrical energy into radio-frequency energy.
7. Antenna system for radiating the radio-frequency energy into space.
16-26
SOUND-EEPRODTJCTION SYSTEMS
A schematic diagram of a typical broadcast transmitting system, sho-wing the general
type of circuit layout employed, is given in Fig. 1. A single studio and a single remote
pick-up point are represented, each such point requiring a duplicate of the equipment
FIG. 1. Broadcasting System Layout
shown, up to and including the relays associated -with the outgoing lines to the various
networks.
The first four items listed above as parts of a complete broadcasting system have been
described in detail in the opening articles of this section, "Audio Facilities for Sound
Systems/* The remaining items listed are more or less peculiar to broadcasting systems
and are covered below.
PROGRAM LINES 16-27
13. PROGRAM DISTRIBUTION SYSTEMS
NETWORK SWITCHING EQUIPMENT. The key stations of a network of broad-
casting stations must provide means whereby the output of any studio may be distributed
to any of the networks or combination of networks radiating out from the city in which
the key station is located. Frequently different programs, coming from different origina-
tion points, are simultaneously sent to the various legs o! the network radiating from the
key station. In order to accomplish these operations switching means are used whidb
permit the connection of a line amplifier across the program bos of the desired program
source.
The facilities for switching are usually such that the proper studio and aetwork line-op
may be arranged previous to "air time" but without actually connecting the studio© in-
volved to their respective networks until a master switch is operated. Upon the proper
cue, or at the proper time, operation of the master switch connects the various studios iBt~
volved to the right networks. The actual switching is seldom accomplished by Biar};iml!y
operating the switches but rather through the medium of conveniently located relays
which are remotely controlled from the operating desk.
BRIDGING AMPLIFIER. The purpose of the bridging amplifier is to isolate the out-
going "radio" lines from one another and to provide a means of connecting any number of
outgoing lines to any program source, at will, without causing any unbalancing or imped-
ance mismatch of the equipment line-up. If two or more outgoing radio lines feeding
different networks, but carrying the same program, were to be connected in parallel and
thence to the output of the program amplifier, then, should any noise, ground, or otber
fault develop on one line, it would affect the operation of the others. By placing a bridg-
ing amplifier (which is, of course, a one-way device) in each line, complete isolation is ef-
fected and there is no possibility that one line will affect others being fed from the same
studio.
The bridging amplifier also permits the connection of any reasonable number of lines
to the output of a given studio amplifier without causing an impedance mismatch whicfe
would adversely affect the operation of the system. To accomplish this connection, tiie
output of the program amplifier is terminated in a resistance of the proper size, thereby
presenting a practically constant load for the amplifier. The input impedance of the
bridging amplifier is then made very high and is "bridged" across the desired program bus
without appreciably affecting the load impedance being presented to the output of tfae
program amplifier.
A bridging amplifier is associated with each of the outgoing lines leading to a local
transmitter or to a network of stations.
BIBLIOGRAPHY
Chinn, H. A., CBS Hollywood Studios, Proc. I.R.M., July 1939, p. 421.
Rackey, C. A., Network Broadcasting, Elec. Bng., January 1941 , p. 16.
14. PROGRAM LINES
Telephone lines are employed for the purpose of transmitting a program from one studio
or station to another station. The facilities involved may be divided into two classes:
(1) local lines for connecting the studio remote pick-up points, such as athletic iieJds,
theaters, and hotels, and also those lines used for connecting the studios to the kxml trans-
mitter; (2) long lines interconnecting a network of transmitting stations throughout the
country.
LOCAL LINES. When the stations involved are In the same city the line connecting
facilities are known as loops. These relatively short lines may, by the employment of
proper terminal equipment, be made to have an essentially flat transmission vs. frequency
characteristic over the entire range of audio frequencies necessary for high-fidelity broad-
cast service (see Section 16, article 18). In order to obtain this desirable feature the
natural attenuation characteristics of the lines, which for tbe most part are cable circmtfi,
are modified at the receiving terminals by means of an attenuation equaliser.
LONG LIKES. If the stations to be interconnected are in different eiti«s the connect-
ing facilities consist of special telephone lines which are either non-loaded open wire or
loaded cable circuits (see Section 17, article 18). Present cable facilities are loaded a*
intervals slightly in excess of 1/2 mile. Amplifiers, equalizers, and phase correctors are
16-28 SOTJND-BEPBODTJCTION SYSTEMS
installed at approximately 50-mile intervals on cable circuits and about 125 miles apart
on open wire facilities. The cable circuits have automatic regulators installed about
every 150 miles in order to keep the loss of the circuit independent of the temperature
along the circuit.
Attenuation equalizers are employed on these circuits just as in local lines. Velocity
correctors (see Section 5, article 10, and Section 17, article 18) are also necessary to com-
pensate for the natural characteristic of the lines which results in an unequal time delay
in the transmission of the various component waves of different frequencies. In circuits
less than 500 miles long these devices would not be necessary, but with present circuit
requirements of 2000 to 3000 miles they are indispensable.
Long-line facilities are available with overall transmission vs. frequency characteristics
that are essentially uniform over the entire audio-frequency range necessary for high-
quality broadcasting.
ATTENUATION EQUALIZER. (See also Section 17, Article 18.) An attenuation
equalizer is bridged across the receiving terminals of a line in order to modify the natural
characteristics of the line so as to provide a circuit having an essentially uniform trans-
mission vs. frequency characteristic over the range of frequencies desired. The device is
connected at the receiving end of the line in order to obtain the best ratio of signal-to-noise
and interference on the circuit.
An attenuation equalizer is an electrical network which introduces a loss at each fre-
quency such that the sum of the line and equalizer losses is the same for all frequencies over
the useful range.
In its most elementary form the equalizer consists of a simple resonant circuit in series
with a variable resistance. The frequency of the resonant circuit is selected so that, with
the proper value of series resistance, the overall transmission characteristic of the circuit
is as uniform as practical.
BIBLIOGRAPHY
Bode, H. W., Variable Equalizers, Bdl Sys. Tech. J., April 1938, p. 229.
Clark, A. B., and Green, C. W., Long Distance Cable Circuit for Program Transmissiom, Bdl Sys,
Tech. /., July 1930, p. 567.
Cowan, F. A., Telephone Circuits for Program Transmission, Trans. Am. Inst. of Elec. Eng., July
1929, p. 1045.
Cowan, McCurdy, and Lattimer, Engineering Requirements for Program Transmission Circuits.
Bdl Sys. Tech. J., April 1941, p. 235.
15. BROADCASTING TRANSMITTER PLANT
A broadcasting transmitting plant consists of audio input equipment, modulator, radio-
frequency generator and amplifier, radio-frequency transmission line, antenna tuning
equipment, and antenna system.
The audio equipment associated with a transmitter plant provides facilities for such
switching operations as are required, microphone and turntable equipment for local pro-
gram origination in an emergency, and amplifiers for increasing the volume level of the
program material received from the line connecting the studios to the transmitter. After
being sufficiently amplified the incoming program material passes to the modulator tube
which modulates the radio-frequency energy generated and amplified by the equipment
supplied for that purpose (see Section 7, article 17; also Section 8, article 4). The re-
sultant modulated radio-frequency energy may either be further amplified or sent di-
rectly to the antenna tuning equipment. The antenna is usually located a relatively short
distance from the building housing the transmitter, and a radio-frequency transmission line
is used to convey the energy from the transmitter to the antenna. The antenna tuning
equipment is usually located at the base of the antenna in an appropriate protective shelter.
STANDARD A-M BROADCASTING TRANSMITTING ANTENNAS. (See Section 6,
article 31.) For standard broadcasting (amplitude modulation in the 540-1600 kc band),
the vertical-radiator antenna is generally used. The use of an antenna having an elec-
trical height slightly in excess of 0.5 wavelength, and operated below the fundamental,
results in the largest field intensities on the horizon for a given radiated power. At the
optimum point of operation the electric field at the receiver resulting from the ground wave
radiated by the antenna may be as much as 40 per cent greater than that obtained from a
0.25-wave antenna radiating the same power. This improvement results from the fact
that more energy is radiated along the ground, where it is desired, and less up in the air.
It does not follow from this, however, that the maximum coverage is secured by an antenna
having this optimum height.
BROADCASTING TRANSMITTER PLANT 16-29
For the low-powered transmitter where the primary range is limited by the field in-
tensity failing below the prevailing interference level, an antenna of the optimum height
would probably result in an increased service area. The cost of such a radiator in compari-
son with the cost of increasing the power of the transmitter sometimes precludes its use,
however.
For the high-powered transmitter the primary range is generally limited to that distance
where "mushing" results from the admixture of the ground and the sky wave, at this point
the strength of the waves being of about the same magnitude. In this case variations in
the sky wave brought about by varying the height of the antenna are far more important
in determining ^the primary range of the station than attendant variations in the ground
wave. The height that is the best operating point for the greatest ground-wave intensity
is not always the best height from the viewpoint of pushing out the incipient fading dis-
tance by the reduction of the sky wave. Hence, the best operating condition for maxi-
mum primary coverage is not necessarily that height which results in the maximum ground
wave. The best height for a given antenna depends upon the attenuation of the ground
wave, which in turn depends upon the effective conductivity of the soil, its dielectric con-
stant, and the frequency of operation. In any event the optimum electrical height is
likely to be between 0.5 and 0.6 wavelength.
The economical advantage of an antenna of this height depends upon the transmitted
power. The initial investment and the cost of operation of the transmitting plant in-
crease with the power, whereas the cost of the radiating structure remains practically con-
stant. At the higher powers this type of radiator represents a good balance between the
two investments.
DIRECTIONAL ANTENNAS FOR STANDARD (A-M) BROADCASTING. The ap-
plication of antenna systems having definite directional properties to broadcasting pur-
poses has been undertaken in a number of instances. Among the circumstances which
have led to the installation of a directional system are: the need for suppressing radiation
in a particular direction or directions in order to prevent interference with a distant station
or stations operating on the same channel; the desire to suppress radiation in a given di-
rection where no audience exists and to reinforce transmission towards the populated area,
as for instance in a station located on a seacoast or to one side of a town which constituted
its principal audience.
A suitable number of vertical antenna elements properly phased and spaced are usually
employed in order to obtain the desired directional characteristic. By the proper com-
bination of these antenna elements and their proper phasing almost any desired direc-
tional pattern may be obtained (see Section 6, article 29). Either vertical- wire antennas
or towers insulated at their base are used for the antenna elements.
F-M BROADCASTING TRANSMITTER ANTENNAS. For f-m broadcasting (fre-
quency modulation in the 88- to lOS-Mc band), a horizontally polarized antenna system
is employed. In general the antenna is non-directional in a horizontal plane. However,
since most receiving sites are located within a few degrees of the horizon, it is advantageous
to utilize an antenna system which directs the radiation towards the horizon. The gain
realized by this practice permits the use of lower actual transmitter power for a given
"effective" radiated power (effective radiated power is the actual power multiplied by the
power gain of the antenna in the direction of the horizon). In practice, the cost of trans-
mitters of various power levels must be balanced against the cost of directional antennas
of various gains in determining the optimum combination.
The f-m broadcasting antenna must be located at a point of high elevation in order to
reduce to a minimum the shadow effect on propagation of hills and buildings. To provide
the best service to an area, a high antenna is usually preferable to a lower one with in-
creased transmitter power.
STANDARD (A-M) BROADCAST STATION TRANSMITTER SITES. The selection
of a good site for a standard (a-m) broadcast transmitter is a very complex problem which
involves many considerations. The site should be selected with the view to providing:
1. Satisfactory coverage of the area comprising the population it is desired to serve.
Usually this consideration will fix the maximum distance from the center of the city that
the transmitter can be located.
2. Maximum coverage of adjacent populated areas consistent with fulfilling the above
requirement.
3. Minimum population in the area immediately adjacent to the transmitter where the
signal is likely to be so strong that special precautions may have to be taken to insure good
reception from other stations.
4. Good soil conditions at the transmitter site. The conductivity of the soil within
several wavelengths of the antenna has considerable bearing upon the efficiency of the
antenna and the nature of its radiation characteristics.
16-30 SOUND-EEPKODUCTION SYSTEMS
5. Good power and program circuit facilities. If possible, two sources of power coming
from different directions should be obtained. In order to obtain better regulation, it is
often advisable to obtain power from a high-voltage line and have a local substation in-
stalled. Because of their relative immunity from storms, telephone lines in cable should
be obtained.
6. Low cost of land. The size of the plot necessary will depend upon the size of the
ground system, the spacing of the towers, and the distance between the anchors for the
guys.
7. Good publicity value and accessibility. These are good assets for a station but may
be overemphasized. Of course, roads leading to the transmitter should be usable in any
kind of weather.
8. Immunity from floods, storms, sleet, etc., whenever possible, and ground suitable
for good tower foundations. In some instances severe storms are localized in certain areas
that can be avoided- Severe storms may cripple power and telephone facilities.
9. Proper location with respect to airports and airways.
10. Proper location with respect to large metal obstructions, buildings, etc.
F-M BROADCAST STATION" TRANSMITTER SITES. The selection of a site for a
f-m broadcasting station entails considerations somewhat different than those for standard
broadcast stations. Many of the differences stem from the quasi-optical nature of the
very-high-frequency-wave propagation. The transmitter site should be chosen with these
factors in mind:
1. The location should be as near the center of the proposed service area as possible
consistent with the availability of a site with sufficient elevation to provide service through-
out the area.
2. The location should provide Hne-of-sight over the principal city or cities to be served.
No major obstructions should be in the path.
3. The site should be so situated that the field intensity in the urban area is sufficiently
great to provide satisfactory service in spite of the generally higher electrical interference
in such areas.
4. Good power and program circuit facilities are required.
5. If the cite is a high building, consideration must be given to the problems of installing
the antenna and the transmitter.
6. Cognizance must be taken of the possible hazard of the antenna to aviation.
BIBLIOGRAPHY
Brown, G. H.f Directional Antennas, Proc. I.R.E., January 1937, p. 78.
Chamberlain, A. B., and Lodge, W. B., The Broadcast Antenna, Proc. I.R.E., January 1936, p. 11.
Lodge, W. B., The Selection of a Radio-broadcast Transmitter Site, Proc. I.R.E., October 1939, p. 621.
16. BROADCAST FREQUENCY ALLOCATION
The frequency spectrum now known to the radio art extends over a wide range and in-
cludes frequencies having widely different characteristics. This spectrum is occupied not
only by broadcasting services but also by other kinds of radio services such, as communica-
tion with ships and aircraft, police services, and amateur, experimental, transoceanic, and
transcontinental point-to-point communication, both telegraph and telephone. Explor-
atory work is still going on in the higher frequencies at the upper end of the spectrum and
is directed in part to determining their usefulness for broadcasting purposes.
The nations of the world have agreed to devote certain portions of the radio-frequency
spectrum to broadcasting purposes. The standard a-m (amplitude modulation) broad-
cast band extends from 540 to 1600 kc per see and is used generally throughout the world.
A band extending from 160 to 265 kc is used in Europe but not in t.M« country for a-m
broadcasting. Several narrow bands in the high-frequency spectrum (above 6000 kc)
are also in use for long-distance a-m broadcasting services. Finally, a band extending
from 88 to 108 Me is used in this country for f-m (frequency modulation) broadcasting.
The wave propagation characteristics of transmissions made in these various bands dif-
fer radically (see Section 10, article 24).
STANDARD BROADCASTING. The term "standard broadcasting" is applied to a-m
stations operating in the band of frequencies from 540 to 1600 ke. Each station is assigned
a particular carrier frequency. On the North American continent the assignable fre-
qraeneies extend throughout the range in 10-kc intervals. Thus the assignments are 540,
550, 560, etc., up to 1600 kc, making a total of 107 distinct channels.
There are three classes of standard broadcast channels: clear, regional, and local.
BIBLIOGRAPHY
^A clear channel is one on which the dominant station or stations render service over
wide areas and which are cleared of objections! interference within their ground-wave
service areas and over all or a substantial portion of their sky-wave service areas.
A regional channel is one on which several stations may operate with powers not in
excess of 5 kw. The ground-wave service area of a station operating on any such channel
may be limited, as a consequence of interference, to a given field-intensity contour.
A local channel is one on which several stations may operate with powers not in excess
of 250 watts. The ground-wave service area of a station operating on any such channel
may be limited, as a consequence of interference, to a gives field-intensity contour.
By assigning adjacent channels in widely separated areas of the country potential in-
terference is minimized. In any one area it is common practice to separate the channels
by approximately 30 kc. This leaves sufficient frequency separation to enable receiving
sets to select one channel to the exclusion of all others in that area,
HIGH-FREQUENCY BROADCASTIHG. By international agreement high-frequency
bands have been allocated for broadcasting services in the vicinity of 6, 9, 11, 15, 17, and
21 Me. Transmissions in these bands are utilized for a purpose and in a manner entirely
different from those in the a-m or f-m broadcast bands. High-frequency transmissions
are primarily intended for long-distance broadcasts to distant colonial possessions, iso-
lated territories, and overseas broadcasting. This type of service depends entirely upon
the sky wave for reception as contrasted to regular broadcast transmissions which utilize
the ground wave for primary coverage (see below). High-frequency transmission to dis-
tant points is not very satisfactory when reception is obtained with the relatively simple
equipment available for the broadcast listener. Magnetic disturbances and atmospheric
conditions seriously affect high-frequency transmissions and cause amplitude and seietrtive
fading and associated deterioration of tonal quality.
F-M (FREQUENCY MODTTLATIOH) BROABCASTEfG. Frequendes above 30,000
kc are referred to as very high frequencies. These wave® are sometimes kaown as quasi-
optical waves because their transmission characterisfcies resemble, in many respects, those
of visible light waves (see Section 10, article 20). As a consequence tfee service range of
a very-high-frequency broadcasting station, evess if located on a high point so that the
waves travel to the receiving station with a minimum of obstacles in their path, is limited
to several tens of miles.
As compared with standard a-m broadcasting frequencies, very high frequencies present
several advantages. Interference caused by natural atmospheric disturbances (static)
is essentially non-existent, and therefore reception is markedly less dependent on seasonal
influences. The service range of the station is more clearly defined and independent of
any normal Heaviside layer conditions. The area over which a very4dgji-fr«quency sta-
tion creates interference with other stations on the same or adjacent frequencies is not
so great, compared to the useful service area, as in standard broadcasting frequencies.
A substantial advantage exists in this respect that is of real assistance in v^ry-high-fre-
quency allocation. The dimensions of the receiving antenna can be small, aad direc-
tional transmission and reception are relatively easy.
The disadvantages of very-high-frequency waves are inherent in- their very nature. The
high absorption during propagation limits tfee service range so- tbat the covering of a large
geographical area by this means oa an economical basis presents a problem. Because of
the quasi-optical character of the very-high-frequency waves there may be propagation
shadows and areas of relatively poor reception, particularly near hilly terrain or high
buildings.
In this country the band of frequencies from S8 to 108 Me has been assigned for very-
high-frequency broadcasting. The assignable frequencies extend throughout the range
in 200-kc intervals. Thus the assignments are 88. 1, 88.3, 88.5, etc,, up to 107.9 Me,
making a total of 100 distinct channels. Frequency modulation, with a carrier swing of
±75 kc, is used. The term f-m broadcasting is applied to this class of service.
Currently in this country there are two classes of f-m stations. Those designated as
Class A are designed to render service primarily to a community or U> a city or town other
than the principal city of the area and the surrounding rural area. Class B stations are
designed to render service primarily to metropolitan districts or principal cities and sur-
rounding rural area, or to rural areas removed from large ©enters of populatkni.
BIBLIOGRAPHY
Federal Communications Commission, Standard* of Good Engineering -Praxes coaming Standard
and FM Broadcast Stations. Federal Communications Communion Rules and Regulations.
16-32 SOUND-REPRODUCTION SYSTEMS
17. BROADCASTING STATION SERVICE
STANDARD BROADCAST COVERAGE. In considering the probable service area
of a standard broadcast station it is necessary to take into account the effects of both the
ground and sky waves which are radiated by the transmitting antenna.
The ground wave (or direct ray) which travels directly over the surface of the earth
from the transmitter to the receiver is unaffected in its propagation by meteorological or
seasonal conditions and is of the same intensity during both the day and the night. The
sky wave (or indirect ray) which traverses the Heaviside layer is subject to a great deal of
variation in strength and character before reaching the receiving point (see Section 10,
article 24).
The radiated energy which follows close to the earth, called the ground wave, is char-
acterized by: (a) high field intensities near the transmitter; (6) attenuation to low values
within a few tens of miles, depending upon the character of the ground, the power and
frequency of the transmitter signal, and the type of transmitting antenna; (c) relatively
steady values.
The energy which is reflected back from the ionosphere (chiefly evident after sunset),
called the sky wave, is characterized by: (a) considerable field intensity at distances of
hundreds of miles from the transmitter; (&) wide variation in field intensity from moment
to moment, from night to night, and from year to year; (c) considerable variation with
latitude of the transmission path and the earth characteristics in the vicinity of the trans-
mitter, and some variation with frequency.
Because of its steady nature and the strong signals obtainable in areas near the trans-
mitter, the preferable service of any station is that obtained from ground waves. The
extent of the areas of ground-wave service is determined not only by the transmitter
power, by the frequency and type of antenna, and by the ground conductivity in the area,
but also by the interference to the desired signal caused by atmospheric noise, man-made
noise, other stations on the same or adjacent channels, or, under certain conditions at
night, by the fading and distortion caused by a mixture of ground wave and sky wave.
Since the intensity of these limiting factors varies widely from moment to moment and
from night to night, the area of satisfactory service also varies.
Since the strong steady ground-wave service is in general available only within a rel-
atively short distance of the transmitter, a considerable part of the country lies outside
such areas. This is particularly true at night, when strong sky-wave signals from distant
stations on the same channel cause considerable interference in many instances and thus
reduce the effective service area from its daytime value. At night in these areas use can
be made of any interference-free sky-wave signals for service, but, because of its wide
variation in intensity and occasional periods of signal distortion, such service is considered
in general less desirable than ground-wave service. The extent of the area of satisfactory
sky-wave service depends upon the interference to the desired signal caused by atmospheric
and man-made noise, other stations on the same and adjacent channels, and under certain
conditions by the fading and distortion caused by a mixture of the station's own ground-
and sky-wave signals. In view of the wide variation in sky-wave-signal level from night to
night, the area in which satisfactory listening can be had on any one night will vary greatly.
The zone in which fading is first encountered is at that distance where the sky wave
becomes of such intensity as to interfere with the ground wave. The primary range of
the station may be extended either by increasing the strength of the ground wave or by
decreasing the strength of the sky wave (see Section 10, article 23). If the receiver is
located within the incipient fading distance an increase in transmitting power above the
noise level improves reception and increases the primary range. In the fading zone,
however, an increase in power beyond that required to produce an average field intensity
sufficient to override noise produces no further increase in service area. This is because the
strength of the ground wave and that of the sky wave are being increased simultaneously
and thus the relationship between them is maintained constant. It is therefore evident
that with the low-powered transmitter the primary range is limited by the field intensity
falling below the prevailing noise level at the receiving point. With the high-power trans-
mitter the primary range is more likely to be limited by fading and attendant objection-
able phenomena since the ground wave will usually be strong enough to override noise out
to and beyond the point where fading begins. For detailed calculations of broadcast
station range see Section 10, article 24.
F-M BROADCASTING COVERAGE. Although some service may be provided by
troposphenc waves, the service area of a f-m broadcasting station is considered to be only
that served by the ground wave. The extent of the service area is determined by the point
at which the ground wave is no longer of sufficient intensity to provide satisfactory re-
FIDELITY EEQUmEMENTS OF BROADCAST SYSTEM 16-33
ception. The field intensity necessary for service in city, business, or factory areas is
generally considered to be 1000 microvolts per meter. In rural areas, on the other hand,
50 microvolts per meter is generally believed to be sufficient for good reception. These
figures are based upon the usual noise levels encountered and upon the absence of inter-
ference from other stations.
The ground-wave-signal range of a f-m broadcasting station is a function of the heights
of the transmitting and receiving antennas, the gain of the antennas, the transmitter
power, the frequency, the ground conductivity, and the dielectric constant. The service
area of a f-m station, just like that of standard a-m broadcasting stations, may be ac-
curately calculated by known methods (see Section 10, article 20). A detailed study of
the service areas possible with f-m broadcast ing stations develops these facts:
1. The service area of approximately half of all United States low-power (100- and 250-
watt) standard a-m broadcast stations could be increased by going to frequency modula-
tion.
2. Standard broadcast stations hi areas of poor soil conductivity would benefit by a
change to frequency modulation.
3. Standard broadcast stations having frequency assignments in the high-freqiiency
end of the band would gain by a change to frequency modulation.
INTERFERENCE TO BROADCAST SERVICE. The strength of the electric field
produced at the receiving location depends on many factors such as the power of the
transmitting station, the nature and efficiency of the antenna system, the distance in-
volved, the nature of the intervening terrain, and in some cases the time of the day and
the season of the year. At a particular receiving location, in addition to the electric field
strength produced by the desired broadcast station, other electric fields will exist which
may hamper or prevent reception, It is not the absolute electric field strength produced
by the desired broadcast station which determines whether reception will be satisfactory;
it is the ratio of the desired field strength to the predominating interfering fields, coupled
with the ability of the receiving set to diseriininate against those interfering fields, which
determines the success of the reception.
Interfering fields may arise from atmospheric disturbances (static), from industrial
electrical interference, and from stations operating on the same or different channels.
The intensity of the atmospheric noise is not constant throughout the radio-frequency
spectrum. At night it varies inversely with the frequency; daytime atmospheric noise
varies approximately inversely as the square of the frequency. The magnitude of the
noise depends upon the geographical location of the receiving point, the season of the year,
and the conditions existing at the receiver.
Industrial electrical interference produced by the operation of non-radio electrical de-
vices is, on the average, inversely proportional to the radio frequency. There are also
present within the receiving apparatus, itself, sources of noise that require consideration:
resistor noise, tube noise, contact noise, and noise associated with the tube power supply.
In general, this receiving-set noise is independent of the radio frequency to which the re-
ceiver is tuned,
CONTINUITY OF SERVICE. One of the prime prerequisites for the successful
operation of a broadcasting station is the absolute continuity of service throughout the
broadcast day. The necessity for such operation arises from the keen competition among
the many stations in this country and the psychological reaction of the average listener
to an interruption in the program service.
This requirement imposes a severe responsibility upon the equipment and on the main-
tenance crew of a broadcasting station, inasmuch as the stations at the broadcasting
centers and those associated with the major chains operate from 16 to IS hours con-
tinuously every day of the year. In planning a broadcasting station many precautionary
measures must be taken and suitable devices must be provided to permit the instant
isolation and replacement of any equipment that becomes defective during the course of
operation.
18. FIDELITY REQUIREMENTS OF BROADCAST SYSTEM
A high-quality broadcasting system is one which acoustically transports the listener in
fancy from his loudspeaker to the studio or auditorium. It must be free from frequency,
non-linear, and velocity distortion. It must not introduce extraneous sounds of annoying
nature or distracting magnitudes.
TONAL RANGE. Complete freedom from frequency distortion implies that the system
should be uniformly responsive over the entire range of audible frequencies. The audible
range of the ear depends upon a great many factors (see Section 12, article 2), the ex-
16-34 SOTJND-REPBODUCTION SYSTEMS
treme limits being in the neighborhood of 16 to 16,000 cycles per second — some 10 octaves.
In practice, few persons can hear this extreme range at the listening levels normally used
in the home (65-75 db above the acoustical reference level of 10~16 watt per cm2). Fur-
thermore, studies seem to indicate that few care to hear this extreme range when listening
to broadcast music.
Several kinds of investigations have been undertaken to obtain data that would be of
assistance in determining the optimum tonal range of a practical system. One series of
tests was based on the acuity of hearing of the listeners. These experiments were con-
cerned only with the physical ability to hear differences in band width; they disregarded
the question of the enjoyment or esthetic appreciation of wider bands. The types of pro-
gram material included a dance orchestra, two symphony orchestras, male speech, and a
dramatic sketch. The observers were engineers who had had extensive experience in
tests of program quality and were considerably more critical than the average radio listener.
It was found that a change of band width from 15 to 8 kc had to be made to be as readily
detected as a change from 8 to 5 kc. These changes, for speech, are just sufficient to have
an equal chance of being detected by listeners having experience in such tests.
Changes in band width were found to be about twice as readily detected with music
as with speech. Thus, for music, the changes that were just discernible half of the time
were found to be 15 to 11 kc, 11 to 8 kc, 8 to 6.5 kc, and 6.5 to 5 kc.
In another kind of test the tonal range preferences of a cross-section of radio broadcast
listeners were studied. As contrasted to the studies that have been made to determine
the ability to distinguish between different band widths, this undertaking ascertained the
tonal range that the average listener considered most pleasant, that is, the method of
reproduction the listener would select in his home when listening for enjoyment. Classic
and popular music, male and female speech, piano, and mixed voices with sound effects
were employed. Every possible precaution was taken during the tests to remove any
possibility of factors other than tonal range from influencing the listeners. A noise-freer
essentially distortionless system was used, and the reproduction level was adjusted in ac-
cordance with the listener's desires.
In these tests the cut-off of both the low and the high frequencies was gradual, in keep-
ing with the type found in actual radio receivers. It was found that listeners preferred a
tonal range whose upper frequency limit was down about 3 db at 5000 cycles, about 20 db
at 8000 cycles, and about 30 db at 10,000 cycles with respect to the mid-range frequencies.
(The experiments did not test the preference for different rates of cut-off but, rather, for
different tonal ranges all having cut-offs of about the same rate as the one mentioned.)
Most listeners preferred a limited tonal range to a wider one even when told that one con-
dition was representive of "low fidelity" and the other of "high fidelity.'*
In practice, broadcast transmitting systems are designed to provide uniform trans-
mission over a wide range of frequencies. A-m broadcast transmitters, for example, are
capable of covering the audio spectrum from 50 to at least 10,000 cycles, with negligible
variations. F-m broadcast transmitters cover a still wider band, extending to at least
15,000 cps. On the other hand, except for a few isolated Instances, commercially avail-
able receiving sets are not capable of faithfully reproducing anywhere near this range of
frequencies.
Intercity network wire facilities having a very uniform frequency characteristic, par-
ticularly at the higher frequencies, can be secured, but their general use is a matter of
economic consideration. For all practical purposes, the overall frequency-response char-
acteristics of a complete broadcasting system is limited by the wire line characteristics.
The rate at which high-fidelity receiving equipment is put into service will, to a great
extent, influence the employment of better wire line facilities between studios and radio
stations.
DYNAMIC VOLUME RAKGE. The dynamic volume range of a sound source of
varying intensity is the ratio of the loudest sound produced to the minfmnm sound that is
distinguishable. In broadcasting and sound recording, the loudest sound intensities are
usually experienced with symphonic orchestras or special sounds such as explosions, gun-
fire, and factory noises (see Section 12) . The mininium. audible sound intensity is a func-
tion of the residual noise level.
i As noted above (article 1), the maximum sound intensities encountered in studios is
about 95 db for music. Furthermore, it was stated that room noise levels of 25 db are
generally considered satisfactory. Thus it is evident that the ma-yin-mm dynamic range
likely to be encountered in original performances is about 70 db (excluding special sounds
which may reach any intensity) . This is a somewhat wider range (about 10 db) than can
bfe accommodated by most complete sound-reproducing systems. It is considerably wider
than the range that listeners prefer.
Very few listening environments are capable of making full use of even a 60-db dynamic
range. In the home, for example, the average listening level is between 65 and 70 db above
POLICE RADIO 16-35
the acoustical reference. The residual noise level, on the other hand, is 43 dfa in the
average residence, and in only 1 per cent of the homes is it as Sow as 30 db. Thus, even in
the quietest suburban homes the noise level is about 40 db below the average listening level
and in the average home about 30 db down. However, the source of the noise is not likely
to be in the same direction from the listener as the radio receiver. Consequently, the
benefits of binaural hearing (article 1, above) will assist the listener in partially disregard-
ing room noise. Nevertheless, at the average listening level, a 60-db dynamic range can-
not be fully exploited by the listener even in the quietest homes.
As a corollary to the question of dynamic range, it has been found, by studies in which a
cross-section of broadcast listeners participated, that listeners prefer* to hear music and
speech at about the same peak levels (as read by a standard volume indicator, see article
4, above). It was also found that the limit of the range of peo& volume levels tolerated
by the largest number of listeners is approximately 8 db (4 db above and below the average
volume level of the program). Even within this 8-db range it appears that changes in
volume level are less annoying when made gradually. The S-db limit refers to the range
of peak or maximum volume levels, not to the range of minimum and maximum sound in-
tensities or "dynamic range." (It is important that this preferred range in peak levels
not to be confused with dynamic range, which was discussed in the opening paragraphs of
this section.)
It was also found that, regardless of the absolute sound intensity at which the listener
operates his radio, he still prefers an even peak intensity level. This is true whether he
is listening to variety, drama, narrative, or musical programs, The peak intensities of
the main program material (but not necessarily background effects) must not fall more
than 8 db below the maximum peak level; otherwise the conditions for easy listening are
violated.
BIBLIOORAPHY
Chinn, H. A., and P. Eisenberg, Tonal-range and Sound-intensity Preferences of Broadcast Lfeteners,
Proc. I.R.E., September 1945, p. 571.
Chirm, H. A., and P. Eisenberg, New Broadcast Program Transmission Standards, JFYac, 1.&JR* 1M7.
Chinn, EL A., and P. Eisenberg, Influence of Reproducing System on ToaaJ-jaaage PiBfereaeas, Prec.
I.R.E., May 1948, p. 572.
Gannett, D. EL, and I. Kerney, Discernibility of (Granges in Program Band Width, B*& S&s. fadt, J.,
January 1944, p. 1.
Seacord, D. F., Room Noise at Telephone Locations, Eiec, B*x~, Jtuae 1939, p. 225; June 194O, p. 232.
POLICE RADIO
By H. F. Micfcd
Police radio systems may be divided into two major elassificaiioiis from an operational
standpoint. The simplest type of system, designated "oae way/' permits communica-
tion in one direction only, from the headquarters station to mobile units. This type of
operation requires a land station transmitter for the headquarters location and a receiver
for each mobile unit. The "two-way" system provides communication from the iiead-
quarters station to mobile units and from mobile imits to headquarters. The equrpsaeat
required for a two-way system consists essentially of a land station taasmittec, one or
more land station receivers, and a mobile receiver and transmitter for each two-way ve-
hicle. In certain installations where all equipment is oa the same freqvteney, or wliere
mobile transmitters are equipped for 1rfro-freqiien.cy operation, a " three-way" system is
evolved permitting car-to-car communicatioii in addition to the two-way previously de-
scribed. Essentially all systems which have been placed in service siace 1942 are of tfae
two-way or three-way type.
Police radio systems may also be divided into two major group© on tfce basis of the
kind of equipment used. Prior to 1940, practically all police radio installations employed
a-m apparatus. Since that date, the vast majority of systems have made use of f-ua
equipment. The only activity in the installation of a-m apparatus is confined to the re-
placement or expansion of existing systems. New systems, almost without exception, are
of the f-m variety.
The scope and complexity of police radio systems vary with the requirements of eaeii
particular installation. A small municipality may operate a single headquarters station
and a small number of mobile units. If conditions at the system control point are ao*
desirable for the local installation and control of the land station, a location providing
advantages of increased elevation and improved noise-level conditions may be selected for
this equipment. This requires remote-control apparatus at the control point and the
interconnection of the control and station locations by means of wire line.
16-36 SOUND-REPRODUCTION SYSTEMS
In larger cities where a great number of mobile units and a considerable coverage area
are involved, fixed station equipments may be located at several points with individual
control from one central dispatching station or from separate precinct control points.
In many cases, individual receivers of the type used in land stations are located at
several advantageous points throughout a city with their outputs feeding back to the
control station or stations over wire line. This greatly increases the talk-back range of
the mobile unit to the fixed station.
State police systems normally involve a multiplicity of land station transmitters and
receivers located strategically to cover desired troop or patrol areas.
A number of state and large city systems also incorporate CW telegraph stations for
zone and interzone point-to-point communication.
In some instances, radio relay equipment is used for the control of remotely located
stations, particularly where topographical conditions necessitate such remote installation
of land station equipment and render impractical the use of wire line interconnection to
the control station.
19. FREQUENCIES
The first police radio systems operated on frequencies just above the standard broad-
cast band with channels in two portions of the spectrum (1610 kc-1730 kc and 2326 kc-
2490 kc) assigned for this purpose. The general plan was to place state systems in the
lower band and city stations on the higher channels. A number of these systems are still
in operation, and essentially all apparatus employing these frequencies is for land-station-
to-mobile communication. These, doubtless, will be gradually replaced by equipment
operating on higher frequencies.
The next portion of the spectrum assigned for police operation was the 30.1-40.1 mega-
cycle band (now 30—50 megacycles) . It was found that these frequencies possessed many
operational advantages for police work: reduction of interference between stations, re-
duced atmospheric and man-made interference, lower transmitter power output require-
ments, and, probably most important of all, the ability to produce practical equipment for
mobile talk-back operation. It was in this band that f-m apparatus for mobile com-
munications made its appearance with its many attendant advantages.
During World War II the use of still higher frequencies by the Armed Forces disclosed
many characteristics which pointed toward the desirability of their use for police communi-
cations systems. Some background of experience gained in the use of 116- to 118-mega-
cycle equipment for relay purposes in police systems, starting about 1940, also gave added
weight to this belief. Experimental work encompassing frequencies in the 160-megacycle
area revealed very favorable performance characteristics for police use. Accordingly,
the Federal Communications Commission has set aside channels in the 152- to 162-mega-
cycle band for the police services. From actual data covering a representative number of
systems in normal operation, it appears that sky-wave or "skip" interference, often caus-
ing considerable trouble in the 30- to 50-megacycle band, is greatly reduced in the 152-
to 162-megacycle frequencies. Smaller antennas are a natural and desirable result of the
use of 152- to 162-megacycle channels with the further advantage that high gain and
directional antennas for land stations are entirely feasible at these frequencies. Atmos-
pheric and man-made interference is still further reduced as compared to the 30- to 50-
megacycle band. Coverage within the normal service area of a 152- to 162-megacycle sys-
tem is more complete, with fewer dead spots, than with lower frequencies. It appears, also,
that still lower transmitter powers will give satisfactory results.
The Federal Communications Commission has also made certain shared assignments for
police service in the 72- to 76-megacycle band. Tests conducted on the 30- to 50-mega-
cycle, 72- to 76-megacycle, and the 152- to 162-megacycle bands indicate that the extreme
coverage range decreases somewhat as the frequency rises but that improved blanket
coverage within the useful range is achieved as the frequency is increased. The 30- to 50-
megacycle channels are characterized by a greater degree of "bending" of the transmitted
signal and, for that reason, seem better suited for applications where greater coverage
distance is required, particularly in hilly or mountainous terrain.
It appears, therefore, that 30- to 50-megacycle channels are best suited for state and
county police systems and 152- to 162-megacycle frequencies for municipal use. The
Federal Communications Commission has also provided bands for police service in various
portions of the spectrum from 450 megacycles to 30,000 megacycles. Complete informa-
tion regarding all allocations of frequencies for police use may be obtained from the May 6,
1949, issue of the Federal Register or from the new FCC Rules and Regulations, when
published.
EQUIPMENT
16-37
20. POWER AND RANGE
There is no fixed formula for the absolute determination of coverage which may be
expected in a police radio system. Local conditions of terrain, antenna elevation, and
noise level are some of the variables that influence such coverage. Transmitter power
output is also a factor, particularly in the 1610- to 1730-kc and 2326- to 2490-kc bands.
However,^ in the higher-frequency channels, antenna elevation and noise-level conditions
are more influential than transmitter power. Table 1 indicates the normal limit of trans-
mitter power in the various frequency bands (plate power input to final stage).
Since communications range is a function of so many variable factors, actual experience
in the planning and installation of police radio systems is the most reliable means of pre-
dicting results. A single land station installation will afford satisfactory two-way communi-
cation for an average city county, provided that the antenna site is carefully selected
from the standpoint of elevation and noise level. Two-way range up to 50 miles with
30- to 50-megacycle equipment is not uncommon with modern apparatus properly in-
stalled. A slight decrease in range may be expected with 72- to 78-iDegacydte and 152- to
162-megacycle equipment.
Table 1
Frequency,
megacycles
Land Station
Power,
watts
1.61-3.0
25-100
100-220
Above 220
2060
50©
&m
To be specified
in authorisation
21. EQUIPMENT
Land station transmitting equipment is of conventional design using standard circuits
and tubes. F-m equipment is normally of the phase-shift type. The same applies to
mobile transmitters.
Land station and mobile receivers are of the superheterodyne variety and are filed
tuned to the assigned operating frequency. Squelch circuits are provided to quiet the
receivers when the associated carrier is not on the air.
Crystal control has become standard for all transmitting and receiving equipment de-
signed for police service.
Power for land station equipment is normally obtained from the regular public utility
service. Frequently gas-engine generating equipment is provided for emergency opera-
tion in the event of failure of the regular power source.
Mobile equipment uses the car battery as the primary power source with either vibrator
or dynamotor units for high-voltage d-c supply.
Since vertical polarization has become standard in police service (30 megacycles and
up), mobile antennas are of the vertical whip type for either side or roof top mounting,
Land station antennas vary somewhat in design but are usually of the J, coaxial, or ground
plane type.
SECTION 17
TELEPHONY
JOHN D. TAYLOR
J^Y CENTRAL-OFFICE EQUIPMENT PAGK
L Manual Systems and Operation 03
2. Mechanical Systems and Operation 08
3. Toll Systems and Operation 36
4. Tandem Systems and Operation 49
5. Auxiliary Service Equipment 51
6. Common. Systems. 51
7. Power Systems. , 53
RADIO TELEPHONE SYSTEMS
8. Applications. 55
9. Transmission and Operational Methods. 61
10. Principles of Two-way Operation 62
11. System Design 64
12. Installations 66
TELEPHONE LINES— TRANSMISSION CON-
ART SIDERATIONS PAOE
13. Types of Plant , 69
14. Service Requirements— Toll 69
15. Service Requirements — ExeJmnge. ..... 78
16. Plant Design — Toll , . 82
17. Flaat Design — Exefa&age 92
PROGRAM SERVICE
18. Program Service.
101
SOBSCKIBEB. STATIONS
19. Substation Eqaipraeafc, 106
20. Subscriber Station Protection 113
21. Private Branch Exehaage Equipment . . . 114
17-01
LOCAL OFFICE
TELEPHONY
By John D. Taylor
TELEPHONY is the art of electrically transmitting speech between two 01 more points.
Telephone facilities are also used for many other purposes, such as the transmission of
broadcasting and public-address programs.
Transmission of speech and other forms of
intelligence is accomplished over wire circuits
or through the air (radio) or by a combina-
tion of both mediums.
The telephone circuit fundamentally con-
si3*8 °f a Device (transmitter) for transform-
« •, j • , i , • i
** *> fch SOimds ^° electrical currents,
which traverse a connecting medium (line or
channel) and react in another device (receiver)
SUBSET
LOOP
FIG. 1. Connection between Two Subscribers
in the Same Office (Courtesy Bell System)
LOOP
LOOP
in such manner as to convert the electrical currents into the original speech sounds.
Switching arrangements of various types and capacities, either manual or mechanical,*
are necessary to connect local or toll telephone circuits together, and a number of auxiliary
circuits, in addition to the
talking circuit, may be em- LOCAL OFFICE LOCAL OFFICE
ployed for a given connec- SUBSET I I SUBSET
tion, depending upon the
types of systems involved
and the length of the con-
nection. The interconnec-
tion of two subscriber lines
(loops) in the same office is
usually quite simple, but for
lines in widely separated
offices the complete interconnecting circuit and associated apparatus may be very complex.
Representative types of telephone connections between two subscribers are shown
schematically in Figs. 1, 2, 3, and 4.
MANUCONNECTiONANICAL
2 Connection between Two Subscribers in Different Offices
^ the Same City (Courtesy Bell System)
OFFICES
if
LOCAL
TOLL
LOCAL
UBSET
* TOLL
CONNECT-
ING
TRUNK
-«_o-
TOLL
CIRCUIT
-y-
TOLL
SWITCH
TRUNK
*»•
-y
/
LOOP
\
\
\
/
SUBSET
LOOP
^-_«. MANUAL OR MECHANICA1 ,
CONNECTION-
FIG. 3. Connection between Two Subscribers in Different Cities (Courtesy Bell System)
5UBSE*
TC
r
)LL OFFIC
E
TRANS-
MITTING
r~
i
1
!
i_
RE-
CEIVING
THROUGH INTERMEDIATE
OFFICES
RADIO TERMINALS
RE-
CEIVING
T<
JLL OhHC
6
4-.~_-
|
/
TRANS-
MITTING
SUBSET
THROUGH INTERMEDIATE
OFFICES
PIG. 4. Connection between Two Subscribers in Different Countries via Radio Channel (Courtesy
Bell System)
* The word "mechanical" is used in this section in a broad sense to include all forms of non-manual
switching.
17-02
MANUAL SYSTEMS AND OPERATION 17-03
In telephone practice the various facilities naturally fall under four main headings:
(1) central-office equipment; (2) land and buildings; (3) telephone lines; (4) substation
eauroment.
CENTRAL-OFFICE EQUIPMENT
^ Central-office equipment, in general, embraces the various switching arrangements,
including auxiliary units of equipment, which are necessary for the interconnection, dis-
connection, control, and super-vision of telephone facilities. Usually, the larger the
telephone system, the more intricate are the equipment requirements.
The evolution of telephone service has been from magneto to manual common-battery
to mechanical Common-battery operation. All these types of operation are now in use,
but the trend in present-day engineering is to mechanize telephone service in order to ob-
tain greater speed, ease, and efficiency of operation and to avoid higher operating costs.
Central-office equipment includes all types of switchboards, both manual and mechan-
ical,^ switch frames and panels, terminating frames and racks, toll terminal equipment,
testing units, power plants, and many auxiliary pieces of apparatus. The equipment is
housed in suitable buildings, and each entire assembly is known as a central office.
Auxiliary circuits and apparatus, such as alarms and indicators, both visual and aural,
designed to call attention to certain operating conditions, monitoring and supervisory
circuits, timing and recording devices, emergency power and ringing circuits, test circuits,
and many other devices, necessary for the proper operation of central offices, are common
to all systems to a greater or less degree, depending on the type and size of system.
1. MANUAL SYSTEMS AND OPERATION
Manual systems include both magneto and common-battery systems, in which tele-
phone operators manually establish and supervise connections at switchboards, using
flexible cords or keying units.
Magneto operation, first employed in the United States, requires operation of a magneto
or hand generator (associated with magneto telephone sets) by the subscriber to signal the
operator for connections and disconnections, and the provision of local battery (dry cells*
at each telephone. Present practice also provides for hookswiteh signaling (with limita-
tions) by the subscriber on magneto lines, if desired, similar to common-battery operation.
Common-battery operation provides for the subscriber to signal the operator by re-
moving his handset * from or replacing it on the telephone set hook,* direct current for
both signaling and talking being supplied to the telephone set from the central-office bat-
tery over the subscriber line.
Manual switchboards are of several types and are made by a number of different manu-
facturers for inter connecting toll, trunk, and subscriber line circuits.
Magneto switchboards employ simple cord and line circuits but, in general, provide
the least desirable telephone service from the standpoint of speed and ease of operation.
These boards are now built with capacities of up to 200 subscriber Hues and are used
principally in small offices, where the majority of the terminating lines extend into rural
areas and have relatively high energy losses. Even here the present tendency is toward
mechanical equipment in new installations and replacements.
Typical full magneto switchboard circuits of the latest type, for a board having a capacity
of 150 lines and 15 cord circuits, are shown in Fig. 1.
FULL MAGNETO OPERATION of such a switchboard is as follows:
In placing a call, the subscriber turns the hand generator crank at his telephone, send-
ing 20-cycle current over his line and operating the switchboard drop (or line lamp cir-
cuit, if furnished). The subscriber then removes his handset from the hook and listens
for the operator to answer. The operator inserts the answering plug of an idle cord cir-
cuit in the line jack associated with the operated drop, opens her listening key, and requests
the called number. Assuming that this number is also a local subscriber's line in this
office, the operator inserts the calling plug (associated with the cord circuit being used) in
the called-number line jack and operates her ringing key, using code ringing as may be
required, to signal the called station. If ringing power is supplied to the switchboard by
a hand generator, the generator crank must also be turned by the operator while operating
the ringing key. The called station bell is actuated by the 20-cycle current sent out over
* The word "handset" is intended to include the older-type telephone receiver and the word "hook"
to include the newer-type telephone-set cradle.
17-04
TELEPHONY
the line, and the operator awaits the called subscriber's answer with her listening key open;
when she hears the subscriber answer she closes her key and disconnects her telephone set
from the connection.
On completion of the call both subscribers place their handsets on the hook, the calling
subscriber turns his generator crank, operating the answering cord ring-off drop and sig-
(a)
|r5oo*n
R
r*
DV * o
TO UNE
**-T~
T
D FRAME I
REPEATING COIL
CUT-OUT KEY
(b)
v BATTERY KEY, TO KEY
TO NIGHT ALARM CODE ALARM
OPERATOR'S
TELEPHONE
(c)
INDUCTION
COI
L
c
^
3 C
1
[^
11
i j
CONTACTS ON 1
LISTENING KEY
-<TRnr
4-t
•v
A
jf
*
MONITOR
REPEATING
COIL
i
VARiSJOR j
^
° 4
GROUPING KEY
FOR POSITION
SWITCHING
| MONITOR KEY ^^IJ „
U&b
L-h/ flS
<")~~A !
1-ffffflP i } 1
R! IT
TO LISTENING KEY
FIG. 1. Full Magneto Switchboard Circuits— Magneto Signaling by Subscriber (Courtesy Stromberg-
Carlson Co.)
(a) Line circuit with drop arranged for code alarm.
(6) Cord circuit^with repeating coil, double clear-out drops, and repeating coil cut-out key.
(c) Operator s circuit, including monitor, varistor, and grouping key circuits.
naling the operator that the conversation is completed. She then removes the plugs from
the line jacks and restores the cord circuit to its idle position.
Central energy (common-battery) type telephones on magneto lines may be made to
operate successfully, using a line circuit, as shown in Fig. 2. This circuit provides service
to a subscriber in a magneto office similar to common-battery operation, but such service
is limited generally to short town lines, not exceeding about 225 ohms conductor loop re-
sistance. The subscriber removes his handset from the hook, sending a surge of direct
current through the repeating coil windings (line side}, the line, and the telephone set.
This surge induces a surge of current in the drop windings of the repeating coil, which are
in series with the line drop. The line drop is operated and the caU is handled from that
point in the same manner as other full magneto calls.
MANUAL SYSTEMS AND OPERATION
17-05
Magneto toll lines are terminated at magneto switchboards in the same type of line
circuit, and the operating is similar to that for local circuits. In the local switchboard,
two pairs of cord circuits are arranged so that the repeating coil can be removed by operat-
ing a key on toll connections, in order to reduce transmission loss, assuming that circuit
REPEATING COIL
5
CENTRAL OFFICE
PROTECTION
FIG. 2. Magneto Switchboard Subscriber line Circuit Arranged for Common-battery Signaling aaad
Talking by Subscriber i,Courtesy Stromberg-Carlson Co.)
noise is satisfactory without the coil for a particular connection. Figure 3 shows typieal
loop and simplex dial trunk and cord circuits for use &t magneto switchboards, which
have trunks to a mechanical office.
WIPE-OUT KEY
DIAL CORD
emeu IT
IMF
\{
C* °500*»JNOH- ^
") INDUCTIVE
H
1
RETARDATION
COIL
REPEATING
CHAL JACK
LOOP DIAL TRUIviK CIRCUIT
JACK -=-
S1MPLEX DIAL TRUNK CIRCUIT
NOTE A! LOOP DIAL MAY fiE CHANGED TO SIMPLEX DIAL TRUNK CIRCUITS &f ADDING REPEATING COIL,
DISCONNECTING RETARDATION COJL, AND MAKING PROPER CONNECTIONS.
NOTE 8*. SIMPLEX DIAL MAY BE CHANGED TO LOOP DIAL TRUNK CIRCUITS Efcf ADDING RETARDATWN
COM., DISCONNECTING REPEATING COIL, AND MAKING PROPER COMN£CDO*4S.
TIG. 3. Magneto Switchboard— Dial Trunk and Cord Circuits (Courtesy Siromberg-CarJsoB Co.)
COMMON-BATTERY SWITCHBOARDS are made in a variety of types and capaci-
ties, both single and multisection (multiple), to meet service requirements a&d are widely
used throughout the United States and foreign countries. The subscriber signals the
switchboard operator by operating the hookswitch (or cradleswitch) of his telephone.
However, in order to provide this more convenient and faster service, the subscriber switch-
board line, cord, and auxiliary circuits are more complex than for magneto equipment.
17-06
TELEPHONY
Single-section common-battery non-multiple switchboards are used principally in the
smaller towns, where magneto service is not adequate. In this type of board each sub-
scriber's line appears in the switchboard jack field only once, since one operator can reach
any jack in the board. Figure 4 shows schematic circuits of a typical board of this type.
The capacity of such a board is up to 200 subscriber lines, 30 toU or rural lines, and 16
universal cord circuits. The capacity may be doubled by operating two such boards ad-
jacent to each other.
MANUAL SYSTEMS AND OPERATION
17-07
Multiple common-battery switchboards are designed for single-office and
cities, where single-section boards are inadequate to meet service requirements. The ca-
pacities of this type of board range from about 600 to about 10,000 lines, thus limiting the
capacity of a single office to about 10,000 lines. For the large cities, requiring more than
10,000 lines, more than one office, each with its own switchboard, is necessary.
Single-office multiple common-battery switchboards are assembled by sections in one
or more line-ups, each section being identically equipped with jack Selds and cord circuits.
The number of sections in an office varies from two to twenty or more, depending upon
TO OTHER
MULTIPLE ^
JACKS AND ]
LAMPS
TO SUPERVISORY LAMP CIRCUIT
SUBSCRIBER Oft RURAL CORD CIRCUIT
— ~ )
INDUCTION COR.
REPEATING
cot.
OPERATOR'S TELEPHONE
FIG. 5. Multisectaon Common-battery Switchboard Circuits — 4000-Hae Commota-battery Talking »od
Signaling (Courtesy Bell System)
the number of subscriber lines served and the traffic load. Each section of switchboard
provides for from one to two and two-thirds operators and from three to eight panels, in
which the multiple jack and lamp strips are mounted. Each subscriber line has oae
multiple jack with associated line lamp in each section, although in some of the older
boards only one answering jack was provided per line. Thus, jack 100 and its associated
lamp in the first section in the line-up are cabled to jack 100 and its lamp in the second sec-
tion, and similarly throughout the board.
Since each subscriber line terminates in the jack and lamp circuit corresponding to his
number, when the subscriber signals the operator to place a call all the line lamps associated
with his line throughout the board light and may be answered by any available operator,
but by only one at a time. When one operator answers a call, all jack sleeves associated
with that particular line have potential placed on them* which causes a click in the ear of
17-08 TELEPHONY
any operator who touches the tip of her plug to the sleeve of any jack associated with that
line. This click warns the operator that the line is busy. The number of line lamps which
are permitted to light on any one line is usually limited to five but may be less, depending
on traffic loads and calling rates. Figure 5 shows the principal schematic circuits for a
typical multiple common-battery switchboard with a capacity of 4000 subscriber lines,
360 toll lines or 720 outgoing trunks, and 17 cord circuits per position,
The provision of a trunking board and special arrangements of subscriber multiple in
the various line-ups makes it possible to increase the capacity of the board to accommodate
up to 5600, 7200, or 10,400 subscriber lines and to provide for a substantial complement of
toll lines and trunks. However, when new central-office installations or sizable additions
to existing manual boards are being considered, present practices require a careful study
to determine the practicability and economies of employing mechanical operation, be-
cause of its many advantages, including integration with the general trend toward uni-
versal mechanized telephone service.
This board is capable of operating as a combined local and toll, local and trunk, or local,
toll, and trunk board.
Multioffice multiple common-battery switchboards of modern design are similar to the
single-office multiple board described above. Some of the older-type subscriber switch-
boards did not provide for multipling the line lamp as well as the multiple jack, so that
the subscriber's lamp signal had only one appearance in the entire switchboard and answer-
ing time was considerably slower than with the multiple-line lamp arrangement.
INTEROFFICE TRUNKS are necessary in multioffice exchange areas to provide for
extending a call from one office to another. In manual operation the calling-subscriber
signal appears at the calling-subscriber switchboard (designated in trunking as the A
board) , the operator ascertains the called number and, either by the call circuit or straight-
forward trunking method, passes the called number to a terminating trunk board (desig-
nated in trunking as the B board) at the called office. An intermediate office (tandem)
may be involved in establishing the trunk connection. The A operator connects the
calling line to the selected outgoing trunk at the A board, the B operator at the called
office connects the B end of the interconnecting AB trunk to the called B board multiple
jack, and the ringing of the called subscriber automatically starts. The cycle of ringing
usually consists of a 2-sec ringing interval followed by a 4-sec silent interval with d-c
potential only impressed on the line. This cycle is repeated until the subscriber answers
or the connection is taken down. When the subscriber answers in either the ringing or
silent interval, relays in the B trunk circuit operate, disconnecting the ringing power
and connecting the trunk circuit talking path through to the called subscriber. Upon
completion of the conversation, a lamp disconnect signal appears before both A and B
operators, in response to both the calling and called subscribers hanging up their hand-
sets, and the connection is taken down.
Call circuit trunking is a, procedure by which the A or toll operator passes a call to a
B (or tandem) operator over a call (order wire) circuit, which is entirely separate from the
trunk circuit being used for the call. When the A operator presses her call circuit key
associated with the call circuit to the desired B (or tandem) office, she is connected directly
to the distant operator's telephone set. After she passes the call to the distant operator,
the distant operator assigns an idle trunk in the group between the two offices and the A
and distant operators connect the trunk to the calling and called lines at their respective
boards.
Straightforward trunking is now the generally accepted method in manual operation
rather than the call circuit method, from which it differs in that the A operator selects the
idle trunk to the called office. She then connects the calling subscriber to the trunk with
an A cord circuit, causing a lamp to light at the distant operator's position. The distant
operator connects her telephone set to the trunk by pressing a key, or the set is automati-
cally connected and the A operator is so informed by hearing a two-tone signal on the
trunk. The call is passed and the connection is established, and during the conversation
the supervisory lamps at both A and B boards remain dark. When the subscribers hang
up their handsets these lamps light and the operators disconnect.
2. MECHANICAL SYSTEMS AND OPERATION
Of the several types of mechanical switching systems now in operation, probably the
Strowger (step-by-step) system, manufactured by the Automatic Electric Co. (and others
under Automatic Co. patents) is most widely known. It was the first type employed com-
mercially (in the year 1892) and is still used extensively today. Other well-known mechan-
ical systems have been developed to meet the needs of the rapidly growing telephone in-
MECHANICAL SYSTEMS AND OPERATION
17-09
dustry, particularly the Relaydiai (Stromberg-Carleoii), Relaymatic (Kellogg Switchboard
and Supply Co.), All-Relay (North Electric Manufacturing Co.), Panel Dial, and Crossbar
Systems (Western Electric Co.). AH these systems have only one purpose, namely, to
switch traffic quickly, accurately, economically, and in a manner satis! actory to the public,
whether it be in a relatively small office or in the largest multioffice exchange area-
17-10
TELEPHONY
THE STRO WGER SYSTEM employs the well-known step-by-step method of operation,
so called because calls are
advanced from the calling
to the called subscriber step
by step, as each digit of the
called number is dialed by
the calling subscriber.
In step-by-step operation,
the principal switching units
involved in a connection be-
tween two local subscribers
are a line switch or line
finder, one or several ranks
of selectors, and a connec-
tor. In addition, if the
connection includes a trunk
between two offices in the
same exchange area, the
outgoing end of the trunk
will terminate in an im-
pulse repeater.
The equipment which
appears between the sub-
FIG. 7.
Self-aligning Plunger Line Switch
Electric Co.)
(Courtesy Automatic
scriber's line terminals and the first rank of selectors is classed as non-numerical, since it
automatically functions as soon as the subscriber's handset is removed from its support
and before any digits are dialed.
Non-numerical switches are of two
major classes — line switches and line
finders. The line switch is individ-
ual to a telephone line and serves to
extend the calling line to an idle se-
lector or connector (forward selec-
tion) , while a line finder is connected
permanently to a selector or connec-
tor and serves to find the calling line
(backward selection) . Line switches
are now seldom employed for public
exchanges but are generally standard
for private automatic exchanges of
100 lines or less.
The line switch may be of two
types, plunger (10-trunk capacity)
and rotary (10- or 25-trunk capacity).
The plunger line switch is a simple
mechanism which automatically con-
nects its calling Line to any one of a
number of trunks leading to numeri-
cal switches (the selector or connec-
tor, which are operated by dial
pulses) . Figure 6 shows a schematic
diagram of the self-aligning plunger
line switch and master switch circuit
and of the wiring arrangement be-
tween trunks and line switches.
Though only three line switches are
shown in this latter arrangement,
there may be from 25 to 100 such
switches in one group. Figures 7
and 8 show views of the line and
master switches.
When the handset is lifted at the « 0 **• A « -j. i. * • ^ -, -,«!,.
FIG, 8. Master S-witch Associated with Self-i,_0 „
Plunger Line Switch (Courtesy Automatic Electric CoJ
telephone, the plunger is thrust into
the line switch bank by operation of
the A and B relays, closing the line and trunk spring contacts and extending the line
through to the selector. The operation of the selector relays maintains the B relay and
MECHANICAL SYSTEMS AND OPERATION
17-11
its plunger operated until the connection is released, the relays then returning to normal.
Operation of the plunger starts operation of the master switch circuit, resulting in the
moving of all idle line switch plungers opposite the next idle trunk. The self-aligning
feature of the plunger reseats it on the master switch guide bar as soon as it is released.
The connector bank terminal associated with the line is also made busy by the selector
placing ground on the control lead.
The rotary line switch is a single-motion device, which may be associated with a tele-
phone line for the purpose of extending the line to any one of a number of idle trunks. This
switch has a shaft carrying wipers, which slide over bank contacts (arranged in a half
circle) to which trunks to the numerical switches are connected. When the line and cut--
off relays are energized by lifting the handset, the switch's driving magnet operates its
TO CONNECTOR 1
SI®
TOO LINES
TO .TRUNK -
SWITCH (g)
FIG. 9. Schematic Diagram of the 200 Line Finder Circuit (Courtesy Bell System)
armature against the action of a fiat spring. At the end of the armature stroke the magnet
circuit is opened, the spring forces the armature back, and the wipers are carried forward
one step into the bank. This action continues until the wipers reach idle trunk contacts,
where they remain until the nest call is originated, when the wipers are moved to the next
idle trunk. It is usually necessary to extend connections by means of wipers and bank
contacts for several conductors which perform signal or control functions in addition to
extension of the transmission path. Thus, each position of the wipers in the bank has
from three to six or more bank contacts, which are simultaneously contacted by separate
wipers when the selection is made. This type of switch is seldom used as a subscriber
line switch since the plunger type is cheaper, but both operate satisfactorily.
Secondary line switches, rotary or plunger type, are now seldom used but were designed
for larger step-by-step offices to combine the traffic from a number of primary groups of
subscriber line switches and direct it to a relatively large common group of numerical
switches capable of handling the combined traffic. Small trunk groups are less efficient
than large trunk groups, and by employing secondary line switches the number of se-
lectors required for the main trunk group need be only large enough to accommodate the
peak load of the combined group instead of each small group requiring enough selectors
to accommodate its own peak load, which usually will not occur at the same time as the
peak loads of the other small groups.
The line finder switch seeks out the calling line from a group of subscriber lines connected
to bank contacts and connects it to a trunk terminating in the first numerical switch of the
17-12
TELEPHONY
switch, train. The line finder switch, permits the use of a simple, economical subscriber
line circuit composed principally of a line and a cutoff relay comparable to those in com-
mon-battery manual systems. These relays function to mark the bank position of the call-
ing line and to cause the allotted line finder to hunt the calling line.
As soon as the bank position of a calling line is marked by operation of the line relays,
a relay of a common relay group (associated with each group of line finders) causes the
proper line finder to hunt, first vertically and then horizontally, until the calling line is
located, whereupon the finder connects its permanently associated first selector (or con-
nector) to the calling line through the finder wipers and
the bank contacts. The cutoff relay of the line circuit then
operates to clear the line of unnecessary attachments and
to free the common group of relays.
A number of line finders are grouped under the control
of a single distributor, which preselects or allots the next
line finder to be used in the next call as soon as the com-
mon relay group is released from the preceding call.
Line finder switches are of the two-motion (vertical and
horizontal) type and usually have capacities for 50, 100,
or 200 lines. In some small exchanges, line finders may
be of the rotary (single-motion) type with capacities of 25
or 50 lines.
Figure 9 shows diagrammatically the switching arrange-
ment between subscriber lines and trunks, and Pig. 10 a
view of a line finder switch,, for 200-line capacity. This
switch has a group of relays mounted on a base, upon
which is also mounted a frame supporting a shaft with
ratchet mechanism for raising and rotating the shaft. The
lower part of the shaft carries four sets of Wipers (one
single-conductor and three two-conductor), termed the
vertical, control (upper bank), upper line (middle bank), and
lower line (lower bank). The vertical and rotary stepping
magnets and the release magnet (which permits the shaft
to return to normal when the connection is released) are
mounted within the switch frame.
A vertical interrupter (pulsing) circuit causes the vertical
magnet (by its armature and pawl engaging the "vertical
hub" ratchet) to elevate the shaft step by step to the
marked level. A rotary interrupter circuit then causes the
^ m^f <ft «• -mature and pawl engaging the
rotary hub ratchet) to rotate the shaft step by step,
until the marked control bank contact is engaged by the
control wiper.
These motions cause the control, upper line, and lower line wipers to engage the cor-
responding contacts of their semicylindrical banks, each of which has 100 sets of contacts
(10 levels and 10 sets per level). To the right of these banks is the vertical bank or com-
mutator, comprising a single row of contacts, over which the vertical wiper moves until
the marked level of the calling line is reached.
The release of the shaft is effected by the operation of the release magnet, which dis-
engages the vertical, rotary, and stationary dogs from their ratchets, permitting the shaft
to return to normal under spring and gravity action.
The impulse repeater is used in interoffice trunks in step-by-step exchange areas having
more than one office. This repeater is required in the outgoing end of each trunk and
functions (1) to make it unnecessary to provide a third (control) wire in each trunk, (2)
to provide talking current to the calling subscriber, (3) to reverse battery to the calling
subscriber when the called subscriber answers, and (4) to repeat dial pulses over the inter-
office trunk so that the impulse circuit will not include both the subscriber's line and the
interoffice trunk.
The two types of impulse repeaters are one-way and two-way. The first type is used'
at one end of one-way interoffice trunks; the second, at both ends of two-way interoffice
trunks.
A diagram of the one-way impulse repeater circuit is shown in Fig. 11.
When the repeater is seized by the preceding switch, the A and B relays operate, and
the B relay connects ground to the control lead C, to protect and hold the preceding
switches in the train and avoid seizure by other switches. R,elay B also operates relays
A-l and B-l in the incoming selector at the distant office, establishing an impulse loop.
(Courtesy
Automatic
Co.)
Electric
MECHANICAL SYSTEMS AND OPERATION
17-13
over the trunk. Relay A, responding to impulses from the calling subscriber dial, in-
terrupts the impulse loop, according to the impulses received, thereby repeating these
impulses over the loop.
When the called subscriber answers, operation of the back-bridge relay of the connector
at the called office reverses the polarity of the current through the holding bridge (relay
F) of the repeater at the calling office, causing relay F to operate. The operation of relay
F causes relay D of the repeater to operate, which reverses the polarity of the curreni now
to the calling telephone, for the purpose of operating coin-collectors or message registers
or of providing supervision of manual calls.
When the handset at the calling telephone is placed on its support, the relays release
and the train of switches is restored to normal.
The selector is a switching device which became necessary for offices of over 100 lines.
In a 1000-termmal system, only a single rank of selectors (first) is required, the first digit
dialed operating the selector switch to connect to the desired hundred group of connectors.
LOCAL OFFICE
DSTANT QPFtCE
NOTE: RELAY »F" MUST NiOT PULL UP UtsTTtL
BATTERY S REVERSED OVER THE TRUNK
THJUW PPi AY
COt!iT*CTS
FIG. 11. One-way Impulse Repeater Circuit — Strowger System (Courtesy Automatic Electric Co.')
In a 10,000-terminal system, two ranks of selectors (first and second) are required. The
first digit dialed operates the first selector to select the thousand group of trunks which
terminate in second selectors, and the second digit dialed operates the second selector to
select the desired hundred group of connectors. Thus, the selector is a numerical type of
group-selecting, trunk-hunting two-motion switch, which requires but one digit for its
operation.
Figure 12 shows a schematic diagram of the selector circuit. The selector has a group
of control relays mounted on a base, which also supports a shaft and ratchet mechanism
assembly for raising and rotating the shaft. The lower part of the shaft carries two sets
of wipers, control (upper) and line (lower). The vertical and rotary (stepping) magnets
and the release^magnet are mounted within the switch frame. The bank contacts are in
two groups of 100 sets of contacts each (10 levels and 10 sets per level) .
When the selector is seized, it functions to hold all preceding switches in the train oper-
ated and guarded until the holding circuit is extended. It sends back dial tone to the
calling subscriber if it is a first selector. It elevates the shaft and wipers in response to
dial pulses and rotates them automatically to connect with an idle trunk in the selected
bank level. It provides a busy signal to the calling subscriber when all trunks in the de-
sired group are busy. The selector is returned to normal, when the calling subscriber
places his handset on its support, by functioning of the control circuit and the release
magnet of the selector.
The connector is a two-motion switch, similar to the selector, and, regardless of the size
of the office, it is always employed as the final unit of step-by-step switch trains.
This switch operates in response to the last two digits dialed of the called number
(directory listing). The first of these two digits is the "tens" and the last one the "units"
digit. The only exceptions to this general principle are the 200-line connector and the
frequency or code-selecting, party-line connectors, where a digit preceding or succeeding
the "tens" and "units" digits is dialed for line group or ringing selection.
Figure 13 shows a schematic diagram of the connector circuit. The connector has a
group of control relays mounted on a base, which also supports the shaft and ratchet
17-14
TELEPHONY
SUPERVISORY RELAY
& NEGATIVE 'BATTERY
OFF -NORMAL CONTACTS
CLOSE WITH FIRST VERTICAL
STEP JUST BEFORE DOUBLE
DOG FALLS IN
CAM SPRINGS (SWITCHED
ON 11TH ROTARY STEP BY
SWITCH SHAFT CAM)
1000W NON
INDUCTIVE
SUPERVISORY RELAY &,
NEGATIVE BATTERY
DIAL TONE AND GROUND
FIG. 12. Selector Circuit — Strowger System (Courtesy Automatic Electric Co.)
RING-BACK TONE
1 CAPACITOR
PER CONNECTOR GROUP
FIG. 13. Connector Circuit — Strowger System (Courtesy Automatic Electric Co.)
MECHANICAL SYSTEMS AND OPERATION 17-15
mechanism assembly for raising and rotating the shaft, step by step. The lower part of
the shaft carries two sets of wipers, the control (upper) and line (lower!, which engage
respective semicircular banks of contacts of 100 sets each (10 levels and 10 sets per level*.
The vertical and rotary stepping magnets and the release magnet are mounted within the
switch frame. One subscriber line is connected to each set of lower line bank contacts.
The pulses of the first digit received (except as mentioned above* siep the shaft and
wipers vertically as many levels as there are pulses. The pulses of the last digit received
step the shaft and wipers horizontally, in accordance with the number of pulse* reeled.
This desired position of the shaft assembly is held by two movable detents, termed the
"double-dog," and a stationary dog.
^ The release of the shaft is under the control of the release magnet, which, in operating,
disengages the dogs, allowing the shaft assembly to return to normal.
The director system was originated and developed by Automatic Electric Co. for large
and complex trim king networks of the Strowger system. Though not used in the United
States to date, it has extensive application in Great Britain, particularly in the London
metropolitan area. It is being considered in the Los Angeles area for certain S X S offices
to meet extended service and automatic toll ticketing problems. The director is ex-
pected to play an important part in nationwide toll dialing, requiring register-sender equip-
ment.
The^director, itself, consists of standard A. E. Co. relays and switches, which store the
subscriber dial pulses and perform various other functions. A director for simple functions
occupies the space of two regular switches, but, being very flexible in design, it may be of
various sizes for specific needs. Wherever used, this unit usually effects savings in se-
lectors, repeaters, and floor space. It can be added to existing S X S equipments as de-
sired.
In operation, an idle director is selected by a director finder and attached to a line finder-
first selector trunk as soon as the line finder seizes the calling line. The director then
functions as an "electrical brain" to:
1. Record the number (pulses) dialed by the subscriber,
2. Analyze the office code digits received and immediately determine the best routing
for the call.
3. Substitute, if necessary, other routing digits, which may differ entirely from the re-
ceived digits. This is known as translation, which permits automatically selected alter-
native routings with resulting trunk savings.
4. Send out pulses, corresponding to the routing code, which operate switches, as though
operated by the subscriber dial.
5. Store the remaining digits, dialed by the subscriber, ustially without translation, and
send out corresponding pulses just after the routing code is sent.
6. Detach itself from the connection upon completion of operation 5 and await the nest
call.
The toll switch train, consisting of a toll transmission selector, a toll intermediate selector,
and a combination toll and local connector, is designed to complete toll calls directly from
the toll board to the subscriber. The toll transmission selector provides increased talking
current to the called subscriber telephone through repeating coil windings and has in-
creased capacity in the talking circuit. It also provides for complete supervision of the
connection at the toll board, and it repeats the dial pulses from the toll operator dial
through to the toll intermediate selector and the toll connector. It has a 400-point bank,
required for additional functions. The toU intermediate selector is similar to the regtilar
selector except that it also has a 400-point bank. The combination connector is not used
for local calls unless all the regular connectors are in use.
Main distributing frames (MDF) and intermediate distributing frames (IDF) provide a
means for properly terminating the outside cables, which carry subscriber liaes and various
types of trunks and toll circuits, and equipment within the office, and cross-coonectiiig
these various circuits and equipments as required.
Multipling of trunks and of switching equipment is so arranged as to provide maximum
access to switches from subscriber lines and from switches to lines, and efficient operation
of trunking and other equipment.
Figure 14 shows a schematic diagram of a trunk layout for a 100,000-line multiofBce
exchange. It will be noted that secondary line switches are employed between the primary
line switches and first selectors and between the first selectors and impulse repeaters, the
object being to concentrate the traffic loads in these sections and reduce to a minimum the
number of first selectors and repeaters required. All manual board services are centralized
at one office for efficient operation. A special switch train is provided to reduce wrong
numbers which may result from careless removal of a handset or accidental jiggling of the
cradle plunger switch. This equipment is not always warranted.
17-16
TELEPHONY
The U suboffice represents a telephone center of light load, located rather remotely
from the other offices. Traffic does not justify a separate group of trunks to each of the
other offices, so that the office is made tributary to office U. To reach a subscriber in the
office, C/0 is dialed, the first incoming switch in the U suboffice being a third selector.
Outgoing calls from this office pass through the main U office.
Multioffice tarunking and other switching in the Strowger system is accomplished, using
in combinations the types of step-by-step switches and repeaters described above and, in
MECHANICAL SYSTEMS AND OPERATION 17-17
addition, many other auxiliary circuits and devices which limited space will not permit dis-
cussing here.
THE PANEL DIAL SYSTEM is a radical change, both in mechanical and electrical
characteristics, from the Stronger system and is employed generally in the largest metro-
politan areas. Great flexibility of operation is permitted by this system as trunk groups
and their sizes are for all practical purposes arbitrary. The time~of establishing a con-
nection is not dependent on the step-by-step dialing process of the subscriber, since, after
all the dialing pulses are received from the subscriber by an intricate mechanism, the con-
nection is rapidly routed to the called line, under control of this same mechanism, with
great speed. The equipment as a whole is necessarily complex.
The principal mechanisms in the system are:
1. The panel-type selector with its banks of line or trunk terminals, which are selected
by vertically moving brushes mounted on bra^s rods.
2. The sequence switch, which has a number of insulating disks mounted on a shaft.
Each disk has a metal stamping on each side, and the entire assembly of disks turns a
step at a time, as directed by the control circuit, with two brushes bearing on each stamp-
ing. By this means a large number of circuit arrangements may be made aa required to
establish the talking connection at the proper time, as determined by the control circuit.
3. The decoder sender is the "brains" of the system. It registers and stores the dial
pulses from the subscriber dial by means of a dial pulse register circuit; it decodes the
numerical digits dialed into a non-numerical selection scheme by chooang the proper
route relay. The route relay controls the selection of an interoffice trunk. The sender
then takes over control, sending out pulses to actuate a train of selectors which establish
connection with the called line. The decoder sender is then released for other calls.
The panel-type selector, from which the system derives its name, performs the same
function in this system that the line finder and selector switches perform in the Strowger
system. The panel-type selector frame consists of several panel multiple banks of sub-
scriber line or trunk terminals, over which the selector brushes slick vertically, and mech-
anism for moving and controlling the selector motion, as shown in Fig. 15.
The panel multiple bank consists of horizontally projecting terminals, arranged in "ver-
tically positioned, rectangular panels or banks, as shown in Fig. 16. Each terminal in
the panel consists of a fiat brass strip extending horizontally through the panel and having
30 projections on each side of the panel and also a soldering lug at each end of the atrip
for wiring. A set of three of these strips, mounticd one above the other and insulated
from each other with impregnated paper, constitute® the tip, ring, and sleeve terminals
of one line. Thus, each line appears horizontally across the face of the panel 30 times,
or 60 times for both faces. The number of lines or trunks provided in the banks varies
in accordance with requirements, present practice with respect to subscriber lines being
to provide 40 lines per panel and 10 panels per frame.
A selector is placed opposite each three vertical rows of line terminals; it consists of a
hollow vertical brass tube on which are fastened ten sets of spring brushes, one set of
brushes for each terminal bank. Each brush has three contacts, normally held apart by
an insulator so as not to touch the lugs or terminals on the terminal panels. Each brush
contact is connected in multiple with the corresponding cant act of the other nine sets of
brushes on the same brass tube or selector, so that any selector may reach any one of the
400 lines in the frame by tripping the proper brush, and the total selector movement will
not exceed one of the ten banks of terminals. In practice, each bank of 40 lines is divided
vertically into two identical banks of the same lines, but with the line numbering in reverse
order (bottom to top and top to bottom of the bank) . This arrangeji&eBt of line number-
ing still further reduces the travel of the selector brushes to reach a particular line and
reduces operating time of the selectors. A trip rod is provided with trip levers for each
bank, so that the brush which is selected to make contact with the calling Ene is tripped as
it starts upward in the calling line bank, the insulator between the brush contacts is with-
drawn, and these contacts make the connection with the calling line terminals when they
are reached.
The multiple wiring between the brushes is contained inside the hollow bras© tube of
the selector and terminates in another set of brushes at the top of the frame, which slide
on bars in the commutator panel and control the selector movement.
The control mechanism of the selector is located at the bottom of the frame. There
are two horizontal cork-covered rolls, extending the width of the frame and driven in op-
posite directions by suitable gears and a motor. Attached to the lower end of each se-
lector tube is a fiat bronze strip or rack, which is close to, but, in the idle position, not
touching, the continuously revolving cork rolls. An eleetromagneticallr operated clutch
is mounted on the selector frame in front of each rack. Energisation of either the up or
down magnet presses the rack against the up or down cork roll, causing the selector to
17-18
TELEPHONY
move up or down as desired. A pawl (not shown) engages in the horizontal slits of the
rack and prevents the selector from slipping down after it has been elevated to^the proper
level. The selector returns to its normal position when released by the trip magnet.
Figure 16 shows the control mechanism.
Rear of seq. sw. &
relays on other
ide of frame
Drive Motor
FIG. 15. General View of Panel Frame — Panel Dial System (Courtesy Bell System)
Control of the up-and-down movement of the selector is obtained either from impulses
coming from the* sender or from connections made on the commutator at the top of the
frame. Panel selector equipment may vary in construction details and wiring, depending
on its assigned function in the system.
MECHANICAL .SYSTEMS AND OPERATION
17-19
Soldering lug
I—L. — I — WJJ__U — U — U — IJJ-H
X^^^ Soldering lugs
X Ad justing screw
Aluminum comb
Panel Multiple Bank
Sddenng lugs
Selector-
Trip
Magnet
-Rack
'Cork Ro»s
Up Drive
Magnet
BoIJer t
Selector Control Mechanism
Driven Disc
- Spring RoJter
Drive
Magnet
Cam Designations
Stotfor
Brush Adjustment
index
Index Wheel
Brush Ctamp
"A" CAM
TYPICAL CAM BRUSH ASSEMBLY
Sequence Switch
FIG. 16. Panel Frame Units, Showing Details—Panel Dial System (Courtesy Bell System)
17-20
TELEPHONY.
TO LINE CIRCUIT
I
The sequence switch. Is vital to panel operation. The control circuits for panel-type
selectors are necessarily complex and must be set up in sequence to cause the various
operations for establishing a connection to take place at exactly the right time. This
switch (Fig. 16) has 24 disks or cams mounted permanently on a shaft, and each disk con-
sists of insulation with a specially shaped metal stamping attached to each side of the disk.
Two brushes bear on each side of each disk. The metal stampings are of different shapes,
so that as the disks turn each brush may rest on the stamping or on the insulation, in ac-
cordance with the position of the switch. This provides a means of establishing con-
nections between brushes or opening and closing circuits in various combinations, as
desired. A fluted metal disk, on which a spring roller rides, is mounted at the end of the
shaft, so that the shaft may be revolved and held hi any one of 18 positions. An electro-
magnet, when energized, pulls this disk against the edge of another continuously revolving
disk and thus causes the shaft to turn one
step at a time for each energization of the
electromagnet.
One sequence switch is associated with
each selector and is located on the right of
the terminal bank, as shown in Fig. 15.
The decoder sender records the pulses
dialed by the subscriber, translates and de-
codes the first group of pulses (office code),
resulting in selection of the proper central
FIG. 17. Interconnection of Decoder Sender office trunk or trunks, and finally controls
Units-Panel Dial System (Courtesy Bell Sys- the brush selection and functioning of the
various selectors and the sequence switch.
The major units consist of a sender, decoder connector, and decoder, as shown in
Fig. 17.
The dial pulse register circuit of the sender consists of a group of relays so connected
as to record the dial pulses and subsequently control the operation of the decoder and
selectors in establishing the connection. Figure 18 shows the portion of the dial pulse
register circuit which registers the first three series of pulses comprising the office code.
The connection of the sender to the subscriber's line operates the AC relay, so that the
P group of relays is connected to the A group. The P group counts the pulses as received
from the subscriber dial. The release and reoperation of the L relay, under control of the
dial, operate the P relays. The A recording relays are operated by the action of the P
relays in such manner that the sum of their numbers is equal to the figure dialed. Thus,
if the first letter of the office name is S, causing seven pulses to be sent, relays A-2 and
A-5 will operate. When the first figure has been recorded, the RA-l relay supplies
ground to the A recording relays, locking them, and releases the P relays. The P relays
are then connected to the B recording relays, which are ready to record the next figure
dialed. This operation is similar for each of the remaining figures dialed by the sub-
scriber.
There are eight groups of recording relays, three for the office code and five for numerical
digits. The last five groups are not shown in Fig. 18, but they are similar to those shown.
When three digits have been dialed, relay CL operates (relay Az operates in place of
relay CL if the first figure dialed is zero). The operation of either of these relays indicates
that the sender is ready for translation. The sender is now automatically connected to a
decoder, through the decoder connector, by connection of the A, B, and C groups of leads
shown in Fig. 18 to the corresponding groups of leads shown in Fig. 19.
The decoder register relay groups, A, B, and C, shown in Fig. 19, then register the
hundreds, tens, and units digits of the office code, stored in the sender. The setting of the
A register relays causes one of the multicontact relays, H-2 to l?-9, to operate; the
setting of the B relays causes operation of the proper T relay, and the setting of the C
relays grounds one of the 10 leads shown at the right in Fig. 19.
Each jET relay has 100 armatures and contacts as indicated in Fig. 19. The 800 con-
tacts are connected to terminal strip punchings, called code points. The operation of an
H relay connects the proper hundred code points to the hundred contacts of the T relays
(ten to each relay). The operation of the proper T relay connects ten code points to the
ten leads from the C relays, and the setting of the C relays connects ground to one code
point.
The code points are cross-connected to route relays (Fig. 19), one of which is provided
for each possible path, which a call may take. Since a particular route relay may be cross-
connected to any code point, so that the selection of a particular route relay is numerical,
the selection operation from this point on need not be on the decimal basis as indicated
above.
MECHANICAL SYSTEMS AND OPERATION
17-21
fr f* • !f y 1S S° desi^ed that it requires certain operations of the district
th ™h selectorS_mdependently of the code point to which it is connected, and thus of
the number dialed in securing it. If the position of a group of trunks i* to be changed on
the selector the route relay must be changed accordingly, but no further change in the
sj stem need be made. Only one route relay is required in each sender for each outgoing
trunk group from the district and office multiple, that is, one for each dialing combination
used in the particular exchange. The route relay, through a cotnbifiatioa of registering
relays, determines the brushes to be tripped and the movements of the selectors which
choose the proper office. Once the proper route relay is selected, the remaining operation
of obtaining the proper office is straightforward. All vacant code points are strapped to-
gether and connected to a single route relay, which will cause the sender to complete the
call to an operator, who will explain to the subscriber that an incorrect number has been
dialed.
17-22
TELEPHONY
MECHANICAL SYSTEMS AND OPERATION
17-23
When the decoder has completed translation, or if translation cannot be completed
owing to trouble, the decoder signals the sender, which releases the decider. Thus, the
decoder is needed only during the time the office trunk is being chosen, but the sender is
needed in the connection until the called subscriber line is connected. More senders will
be required than decoders, the usual ratio being about 400 senders to not over 10 decoders,
although this ratio varies with the traffic load.
IN PANEL DIAL OPERATION each subscriber line terminates on a line finder frame
for handling outgoing calls, and a final frame for handling incoming calls, as shown in Fig,
20. When a subscriber lifts his handset to call, direct current from the central-office
battery flows through his line and operates the associated line relay, at the same time
making his line busy to any selector on the final frame. The operation of the line relay
causes an idle line finder selector associated with the bank of terminals in which his line
appears to move upward until it finds the calling line; this relay also causes the trip rod in
that bank to trip the proper brush of the moving selector, after which the trip rod is im-
mediately reset.
Simultaneously with the motion of the selector, the panel link circuit is selecting the
district selector associated with the line finder selector, and also an idle sender. The
panel link frame is also similar to the panel type selector frame, but with different details
to suit its functions. The frame is divided into two equal parts vertically with the sender
selectors on the left and the district selectors on the right. Each district selector is wired
directly to its corresponding sender selector.
In practice, the district selector when released from a call selects the next idle line finder,
while the sender selector remains where it is unless near the top of the bank, in which case
it returns to normal position.
When the line finder reaches the calling line and the sender selector has found an idle
sender, dial tone is sent back to the calling subscriber.
The action of the sender is described in detail. The dial pulses are stored in the dial
pulse register circuit, the first three digits serving to connect tfee proper route relay ti© the
sender and thus set the proper registering relays in the sender, at which point die decoder
is disconnected from the circuit.
The sender is then prepared to cause the district selector to choose an interoffice trunk
to an incoming frame. The district selectors are typical panel-type selectors, except that
every eleventh terminal and an additional one between the two groups of five at the top
of each bank is arranged as an overflow terminal to stop the motion of the selector when
all ten trunks below it are busy. The trunks can be used in larger groups than multiples
of 10 by making the intermediate overflow terminals busy, In which case the selector will
pass over them, or groups of five trunks are available at the top of each bank.
If 450 trunks are not enough to provide the necessary trunks to all the offices in the
exchange area, a group of office selectors is employed to care for all the trunks outgoing
from the office. The calls are then routed by the district selector to the proper office
selector and thence to the incoming selector of the called office.
The movements of the selectors on both district and office frames are guided by a re-
verse control method. As the selector is driven upward by the cork roll, it sends back
one pulse to the sender each time a brush moving on the commutator (at the top of the
frame) makes contact. Commutators for the various types of selectors are shown in Fig.
21. The pulses are counted by the sender, and, when the number of pulses indicates to
the sender that the selector has moved to the proper position, tiie sender opeas tfee up-
drive magnet circuit, stopping the selector motion.
The first selection on either the district or office frame involves the tripping of the proper
brush. If, as shown in Fig. 20, the desired trunk appears on the fourth panel from the
Line Panel
Finder Fr. Link Fr.
Catling
{Subscriber
District Fr.
Incoming Fr. Final Fr-
FIG. 20. Typical Panel-type Connection— Panel Dial System (Courtesy Bell System)
bottom, the district selector will first move up a distance of four segments on the >, A bar of
the commutator (Fig. 2 in Fig. 21). At that point the selector will be stopped, the se-
quence switch will be turned two steps (from position 4 to 6 in Table 1), changing tfee
17-24
TELEPHONY
fundamental circuit to prepare for the next operation, and the trip rod will be rotated
into position to trip the fourth brush. The selector is now started upward again by the
sender, and sends back a pulse for each bar on the B bar of the commutator, each of which
represents a distance of ten trunks. Thus, the upward movement of the selector to the
proper trunk group is controlled by the number of pulses sent to the sender from the B
bar. When the selector reaches the proper group, the sequence switch is again turned
two steps (position 6 to 8 in Table 1) and the selector moves up slowly, testing each trunk
in the group to find an idle one— a process known as hunting.
^•Thoohu^tiug process is common in panel operation. The connections are shown in
7£\T '-.f connections marked 8 being closed, since the sequence switch is on position 8
(I able 1). If the L relay is operated, the up-drive clutch is energized by current flowing
to ground^nrough the L relay left-hand contact, and the selector moves up. As long as
MECHANICAL SYSTEMS AND OPERATION
17-25
the sleeve contact of the selector brush is grounded, the L relay is operated through contact
7 1/2/8- Since the sleeve contacts of busy trunks are grounded and those of idle trunks
are not grounded, the selector will move a small distance beyond the last busy trunk.
However, even here the L relay is grounded through the commutator brush and the G bar
of the commutator. The reason for this slight extra movement is to allow the holding
pawl on the selector rack to engage the correct slot.
Sleeve Terminals
of Trunks
Sleeve Contact
of Tripped Brush
FIG. 22. Selector Circuit for Hunting Idle Trunk — Panel Dial System (Courtesy Bell System)
When an idle trunk is found, the sequence switch turns to position 10, until the con-
nection is completed, the changes necessary in the control circuits being made by other
sequence switches located on the incoming and final selector frames.
Table 1. Operations of District Sequence Switch
Position
Corresponding Circuit Condition
Position
Corresponding Circuit Condition
I
Normal
10
Selection of brushes, groups, etc..
2
Selecting an idle sender
beyond the district selector
3
Waiting for sender
11
Waiting for sender
4
Selecting brush
12
Talking (non-loaded trunk)
5
Waiting for sender
13
Talking (medium-loaded trunk)
6
Selecting group
14
Waiting for operator to answer
7
Waiting for relays
15
Talking to operator
8
Hunting idle trunk
16
All trunks busy
9
Waiting for sender
17
Operating message register
18
Returning apparatus to normal
These selectors are also of the panel selector type, differing only in details. The final
selector frame has capacity for 500 lines, thus requiring 20 final frames for a 10,000 sub-
scriber line office. The incoming selector frame must then hold 20 groups of trunks,
which can consist of 24 trunks and an overflow terminal. This arrangement, which is
employed in all offices, is shown in Fig. 23. The sender circuit is so arranged that either
0 or 1 in the thousands digit causes brush 0 to trip, while the combination of the first two
numbers determines the proper group for the selector to hunt in. When an idle trunk to
the final selector is found, the second or hundreds digit determines which brush will be
tripped, while the tens digit determines in which group the called line appears. Final
selectors are directed rapidly to the proper group of ten; when the proper group is reached,
the clutch on the up-drive roll is released by a change in the setting of the sequence switch
and !/4 usual speed is substituted as the motive power. The final selector tests the line
on which it stops, and if it finds the line busy it returns to normal and sends back a busy
tone to the calling subscriber.
If the called subscriber has a private branch exchange (PBX) with several trunks, the
final selector will hunt for an idle line if the called number is busy exactly as it hunts for an
idle interoffice trunk.
Many special provisions must be made in any installation for party lines, message rate
service, rapid testing, and other special conditions that arise, but such arrangements will
not be considered here.
17-26
TELEPHONY
THE CROSSBAR SYSTEM is the latest Bell System development in mechanical switch-
ing. It differs radically from the Strowger (step-by-step) and the panel dial systems ^in
construction, operation, and control, but it is so designed that it functions satisfactorily
with all other types of switching, whether mechanical or manual. The crossbar system
offers important improvements in switching, both in operation and maintenance, over the
step-by-step and panel systems, but it does not necessarily replace existing installations or
additions to these older systems.
Only the most important functions of the crossbar system can be discussed in this
handbook, owing to space limitations.
The crossbar system has two outstanding features, the crossbar switch which is used for
all major switching operations, and the marker system of control which is used in establish-
ing all connections throughout the crossbar office. The apparatus consists principally of
crossbar switches of the relay type and multi-
contact and other type relays generally em-
ployed in telephone systems. The switching
circuits are wired to the contacting springs of
the switches, and the circuit closures are made
when the contacts are pressed together by op-
eration of the electromagnets.
The use of relay-type apparatus economically
permits having twin contacts of precious metal
throughout, insuring reliable operation for the
low values of speech and signaling currents in-
herent to telephone systems. The very short
mechanical movements and small operating time
intervals required in crossbar switch operation
permit a reduction in control equipment over
the slower-moving, older-type systems, thus
resulting, in the use of large switch and relay
assemblies on unit-type frames, factory wired
and tested. In the design of the switching
frames and associated control circuits, it has
been possible to standardize a relatively few
types of equipment units, thus simplifying manu-
facture, merchandising, and operating company
engineering.
The marker, composed mainly of relays by
means of which it controls switching operations,
has many advantages, one of the most important
Brush
4
3
2
1
0
Fr
Ccntr;
I neon
ning
Group
Brush
4
3
2
n
nal
Group
95CO
9999
3
2
1
0
3
2
1
0
3
2
4900
4999
4B12g
9000
9499
esoo
8999
8000
8499
750O
7999
4BOO
4899
7000
7499
650O | 6999
600"
6499
E50O ! 5053
47OO
4799
fOOO | 5499
40CO
4491
0
3
2 Z
1 £
0 M
3
2
1
i=n
»-< o
Trunks to Final Selectors
3SOO
3000
4600
4699
2CCP
3499
250C
2990
ccco
24S9
1SCO
1999
j
4599
==^?
1000
1499
050O
0999
oooo
0490
45fl£~
Tsos
M>
am
1 Office
ing Lmi
<&>
— II
1 Trunks to Final Selectors
on Final Frame for Lines 0000-0X99
FIG. 23. Trunk and Subscriber Multiple on
Incoming and Final Selectors — Panel Dial
System (Courtesy Bell System)
being the completion of its complex functional processes in establishing a call in less than
one second. The markers are connected momentarily, by means of multicontact relays,
to various switching units of the office to guide the completion of calls through the
crossbar switches. The marker system provides for an attempt automatically to establish
a call over alternative paths when all the normal routings are busy or trouble is encoun-
tered; the marker will detect, record the location and nature of such troubles, and indicate
their presence to an attendant by operating an alarm. The marker design also facilitates
the introduction of new service features and operating changes as desired, since the main
control features of the entire system are incorporated in a small number of markers.
The crossbar switch, which gives the system its name, is the basic switching unit of the
system. Figure 24 shows a front view of a 200-point switch. Fundamentally, this
switch contains (1) 10 separate horizontal circuit paths, (2) 20 separate vertical circuit
paths, and (3) an electromagnet for each horizontal and each vertical path, so that the
operation of any horizontal and any vertical magnet in sequence will connect a horizontal
and a vertical path together at one of the 200 cross-points. The 10 horizontal paths are
controlled by 5 horizontal bars each actuated by a selecting magnet, and the 20 vertical
paths are controlled by 20 vertical bars each actuated by a holding magnet. Any set of
contacts may be closed by first operating the selecting magnet corresponding to the hori-
zontal row in which the contacts are located, and then by operating the holding magnet
associated with the particular row of vertical contacts. The holding magnet will hold
the contacts closed until the connection is released, but after it is energized the selecting
magnet returns to normal until called upon to operate on another call. Thus, 10 sets of
contacts may be made at one time through the switch, one for each horizontal path.
Figure 25 shows in detail a portion of the selecting mechanism of the crossbar switch.
The 10 sets of contacts in each vertical row are associated with the vertical or holding bar
of that row. Each horizontal or selecting bar has 20 flexible wire selecting fingers, mounted
MECHANICAL SYSTEMS AND OPERATION
17-27
at right angles to the bar, one finger for each vertical row of contacts. When, a selecting
bar is rotated through a small arc by its magnet, the selecting fingers move up or down into
position, depending upon the direction of rotation of the bar. When a holding bar in a
FIG. 24. Crossbar Switch— Front View — Crossbar System (Courtesy Bell System)
particular vertical row is operated by its magnet, it will bear against the particular selecting
finger which has been moved into position in its row, and the finger will be pressed against
the operating spring horizontally in line with it. Thus, the operating spring will be pressed
against the contact multiple (fixed contact spring) and the circuit path will be closed at
that point.
ADJUSTABLE
SUPPORT FOR
SELECTING
FINGER
OPERATING SPRING
CONTACT MULTIPLE
**A
ARMATURE
FIG. 25. Crossbar Switch Selecting Mechanism — Crossbar System (Courtesy Bell System)
The selecting bar and all its fingers except the one being held against the operating
spring will be released as soon as the holding bar operates. When the connection is re-
leased, the holding bar returns to normal and the held finger returns to its idle position
17-28
TELEPHONY
midway between, but slightly to the right of, two sets of operating springs. At those
points along an operated vertical bar where the angers are not operated by the horizontal
bar, the fingers are pushed in between each two sets of operating springs and thus do not
bear against these springs. Only one finger is operated at one time for a given vertical
bar.
The selection operation is performed by five horizontal bars, each of which will select
one of two horizontal rows of operating springs, depending on the direction of rotation of
the bar and consequently the selecting fingers. Figure 24 shows two magnets at the end
of each horizontal bar, one causing the fingers to move upward and the other causing
them to move downward. After release, the horizontal bar is restored to its mid or idle
position by centering springs at the ends of the bars and adjacent to the magnets.
The vertical units of the crossbar switch each have 10 sets of operating springs in vertical
rows with one vertical or holding magnet at the bottom of the row which actuates one
vertical bar or armature extending the height of the 10 sets of contacts. Each set of
contacts may consist of three, four, five, or other numbers of pairs of springs in horizontal
spring pile-up or assembly, depending on circuit requirements. Figure 24 shows four
pairs of springs per set of contacts. One twin contact spring of each pair is stationary and
designated contact multiple; the mate or operating spring of the pair is pressed against
the contact multiple, when operated. This contact multiple spring is made of one piece
of metal, insulated from the mounting and extending the full length of a vertical row of
contacts. Wiring lugs are formed at the lower end of these vertical metal pieces, facing the
rear, to which are wired the lines or trunks of the vertical circuit paths. On the front and
at the lower end of these pieces projections are provided for testing purposes. The mate
or operating springs extend to the rear of the switch, where wiring lugs are provided and
may be strapped horizontally to the corresponding springs of adjoining vertical units,
thus extending the horizontal paths across the switch verticals, or to adjoining switches.
The switch may have "off normal" contact spring assemblies, if required, associated
with each selecting magnet which operates them to perform various circuit functions.
The 200-point crossbar switch is 9 x/4 i^- high and 30V2 in. long. A 100-point switch
with 10 verticals is also available.
The multicontact relay used in the crossbar system and shown in Fig. 26 resembles in
design the vertical unit of the crossbar switch. The relay is provided with 30, 40, 50, or
FIG. 26. Multicontact Relay — Crossbar System (Courtesy Bell System)
60 sets of individually insulated contacts, normally open, but closed when the relay mag-
nets are operated. Each relay has two separate magnets, armatures, and associated groups
of springs. By operating the magnets independently, the unit can be operated as two
separate relays, each closing 15, 20, 25, or 30 sets of contacts, or if both magnets are en-
ergized in parallel the full number of contacts of the unit are closed. All contact springs
have twin contact surfaces of solid bars of precious metal because of heavy duty require-
ments. This relay is used mainly in the common connector circuits, where a large num-
ber of leads must be connected simultaneously to a common circuit.
" New and improved general-purpose small relays of the XJ and Y types are used in the
tsrossbar system. These relays permit the use of up to 24 springs in one assembly, pro-
MECHANICAL SYSTEMS AND OPEEATION
17-29
viding for various combinations of transfer or simple make and break contacts. The
springs are equipped with twin contacts of various contact metals, depending on the
characteristics of the circuits controlled by them. The Y relay has a slow release action
obtained by copper or aluminum sleeves over the relay core.
CROSSBAR OPERATION may be more readily understood from the block diagram
of the functional arrangement of the principal equipment units of the system which are
involved in a connection between two subscribers, as shown in Fig. 27. The three main
FIG. 27. Functional Arrangement of Equipment Units — Crossbar System (Courtesy Bell System)
types of equipment units are: (1) the district junctors and incoming trunks, which supply
battery to the transmission and supervisory circuits; (2) the crossbar switch frames; (3)
the common control circuits and the senders and markers.
The district junctor and incoming trunk circuits are composed mainly of small relays.
The district junctor furnishes talking battery for the calling subscriber and supervises
the originating end of the connection. The incoming trunk circuit controls the ringing of
the called subscriber bell, furnishes talking battery for the called line, and supervises the
terminating end of the connection.
The switch frames, consisting principally of crossbar switches, provide the means for
switching between the subscriber lines, district junctors, and incoming trunks, and also
for switching these district junctors and trunks to senders.
The senders consist chiefly of small relays, and their function in crossbar is comparable
to that of an operator in manual operation. The subscriber sender registers the called
number from the subscriber dial pulses and transmits the necessary information to the
markers, to the terminating sender, and to the manual operators (in manual offices) for
completing connections to the called line. This sender also controls operation of the
selectors in distant panel offices. The terminating sender receives the numerical digits
of the called number from the subscriber sender of any panel or crossbar office and trans-
mits the required information to the terminating marker for setting up connections to the
called line.
The markers are the most important control circuits in the crossbar system. They
comprise both small and multieontact relays and are of two types, one for originating and
one for terminating traffic. Since their operating time is less than 1 sec, only three or
four markers are needed in the average size office.
The originating marker determines the proper trunk routes to the called office. It has
access to all outgoing trunk circuits and all crossbar switch frames used in establishing
connections to the called office trunks. The marker records pulse information, tests the
17-30
TELEPHONY
trunk group for an idle trunk to the called office, tests for and marks or reserves an idle
path through the switch frames, and finally operates the proper crossbar switches to es-
tablish a path from the calling subscriber line to the outgoing trunk circuit. The lowest-
numbered available paths are always selected in order to reduce selection time and in-
crease operating efficiency.
Trunk selection is made by the marker through route relays, of which there is one for
each called office routing. This relay is so wired as to direct the marker to the called
office trunk group and indicate the number of trunks in the group; also to indicate the
office link switch frame on which the trunk group appears and the type of called office,
which is also indicated to the sender. Route relays may be assigned to any office trunk
group, and other changes may be made, as required.
The terminating marker performs similar functions in the terminating office, establish-
ing a path between the incoming trunk circuit and the called subscriber line. This marker
has access to all the subscriber lines terminating in the office and to all crossbar switch
frames used for connecting to subscriber lines. It records pulse information, tests the
called line to determine whether it is idle, tests for and marks an idle path through the
switch frames, and finally operates the proper crossbar switch magnets to establish con-
nection to the called line.
The marker, in testing and connecting the called line, employs a marker group con-
nector circuit and block relay frame in which the called line appears. Each subscriber
line has three test terminals on the block relay frame, and a number group connector will
usually have access to the test terminals of several hundred lines. The marker deter-
mines from these test terminals whether the called line is busy and the identification of the
proper line link frame and horizontal group of line links which have access to the called
line; also the type of ringing required is determined from circuit conditions on the test
terminal.
There are also common control circuits, associated with the line link and sender link
frames, for controlling the operation of the switches on these frames. In addition, there
are common connector circuits, composed mainly of multicontact relays, which are used to
connect the markers (1) to their respective senders, (2) to their associated switch frames,
and (3) to the subscriber line test terminals.
The line link frames, although shown separately in Fig. 27, are, in a given office, used
for both originating and terminating traffic. After the talking connection has been es-
tablished between subscribers (see Fig. 28) , all the common control circuits, including send-
ers, markers, connectors, line link control circuits, sender link frames, and their associated
CALLING
TELE-
PHONE
a
LINE
LINK
FRAME
i~r
DISTRICT
JUNCTOR
CALLING
TELEPHONE
TRANS-
MISSION AND
SUPERVISORY
RELAY
EQUIPMENT
DISTRICT
LINK
FRAME
«rt.
OFFICE
LINK
FRAME
•%J-
INCOMING
TRUNK
CALLED
TELEPHONE
TRANS -
" MISSION, "
SUPERVISORY
RELAY, AND
RINGING
EQUIPMENT
INCOMING
LINK
FRAME
LINE
LINK
FRAME
4o-of
CALLED
TELE-
PHONE
o
FIG. 28. Completed Talking Connection — Crossbar System (Courtesy Bell System)
control circuits, will have been released, and the talking path will be maintained by the
holding magnets of the crossbar switches, which are used on the link, district, office, and
incoming link switch frames. These holding magnets are held operated under control of
the supervisory relays in the district junctor and the incoming trunk circuits and are re-
leased only when the subscribers hang up their handsets.
The establishment of a connection with the crossbar switch is shown schematically in
Fig. 29T in which 20 vertical units are connected to 20 subscriber lines and 10 trunks are
strapped horizontally across the switch. With this arrangement, any one of the 20 lines
may be connected to any one of the 10 trunks by closing the contacts at the proper cross
point. By adding a second 200-point switch with 20 additional lines connected to its
verticals, and extending the trunk strapping through both switches, 40 lines are given
access to the 10 trunks. Thus, by adding other switches in this manner, the number of
lines having access to these 10 trunks may be further increased.
A line link frame comprises primary bays and secondary bays. Each primary bay
terminates 200 subscriber lines (10 primary switches with 20 lines each), but the number
of primary bays per frame may be varied within limits to meet traffic requirements. The
secondary bay contains secondary switches; the bay is divided vertically in the center,
so that there are 10 switches, each with 10 verticals on the left of center and the same
arrangement on the right of center of the bay. The switches on the left have their ver-
MECHANICAL SYSTEMS AND OPERATION
17-31
TO ro
TRUNKS
ticals connected to line junctors which are used for terminating traffic, and those on the
right have their verticals connected to district junctors which are used for originating
traffic. At the bottom of the secondary bay is a cabinet containing control circuit relays,
and just above this cabinet
are the multicontact relays _ FROM 20 LINES
which connect the control
circuits to the crossbar
switches.
Since each subscriber in
an office has only one cross-
bar appearance and that on
a vertical unit of a primary
crossbar switch, both origi-
nating and terminating calls
are completed by means of
the same line link circuits
serving that particular
switch. Thus, all originat-
ing traffic from any of the
20 lines on a primary switch
flows through the associated
10 line links to the 100 district junctors, and all terminating traffic to these 20 lines flows
through the same 10 line links from the line junctors, as shown in Fig. 30.
The arrangement shown in Fig. 30 is also used in the originating and terminating sender
link switch frames, where the circuits reached are non-directional, that is, where any one
of the circuits wired to the frame and available for selection can be used for establishing a
connection.
Where it is necessary to provide greater flexibility and efficiency in trunk groups than
is possible with the arrangement shown in Fig. 30, two primary and secondary switch
) i ;
> -
i i
\ i
> «
T e
5 ?
1
D I
!
.
= r
i u
* i.
> i
S 17 18 19
tit ..,
1
1 > n
1 -
\
"
fc -5
» -1
!
I
1
°j
FIG. 29. Simple Trunking Arrangement with a Single 200-point
Crossbar Switch — Crossbar System (Courtesy Bell System)
SUBSCRIBER
LINES
DISTRIBUTING
FRAME
FRAME SERVES
ISO TO 70O LINES
DEPENDING ON
TRAFFIC
TO
DISTRICT
JUNCTOR
FRAME
FRAME HAS
ACCESS TO
100 DISTRICT JUNC-
TORS, 100 LINE
JUNCTORS
PRIMARY SECONDARY
FIG. 30. Single Primary-secondary Trunking Arrangement — Crossbar System (Courtesy Bell System)
frames are employed, as shown in Fig. 31. This layout shows an incoming link frame to
which incoming trunks are connected, and a line link frame to which subscriber lines are
connected. These two frames are operated in tandem for establishing the terminating
connections between the incoming trunks and are called subscriber lines. As shown, 100
incoming trunks are connected to the 100 horizontal paths of the 10 incoming link frame
primary switches, 10 trunks per switch. Although only 200 lines (20 lines on each of 10
17-32
TELEPHONY
primary switches) are indicated in Fig. 31, 150 to 700 subscriber lines mav appear on the
verticals of the primary switches of the line link frame.
Referring to Fig. 31, the connection of a particular incoming trunk to a particular called
line requires the selection of an idle path through the incoming link and line link frames.
This path will consist of an incoming link, a line junctor, and a line link. The incoming
trunks on each of the primary switches have access to 20 incoming links appearing on the
20 verticals of the switch. These 20 incoming links are distributed over the 10 secondary
switches of the incoming link frame, two links to a switch and one link to each half switch.
In order to provide for the distribution of the 20 incoming links over the 10 secondary
switches, the horizontal paths of the secondary switches are separated between the tenth
and eleventh verticals, thus providing 20 instead of 10 horizontal paths on each switch.
The incoming links on each half of these secondary switches have access to line junctors
appearing on the verticals of these switches. These junctors are, in turn, distributed over
INCOMING LINK FRAME
PRIMARY SWITCH 9 SECONDARY SWITCH 9
LINE LINK FRAME
SECONDARY SWITCH 9 PRIMARY SWITCH 9
5
1
0
Zt/5 x
5-1 '
9i 9
r}
4- TO OTH
? > LINE
! LINK
• FRAME
9
9
2LL\.
0
L
R
i
0
L
.9
I*
R
,9
0
\
0
0 ,
0 ,
9
0 .
9 .
0 .
9
>i
o igJ
T
COMING
LINKS
— *>
— »
— »
RIGHT
OFPR1
SWITCH
HALF"
MARY
IES
<ER
ES
i i
lO^DISTRICT
JUNCTORS
^.LINE
JUNCTOR
SWITCH 0
LINKS
20 SUBSCRIBER
LINES
1 SWITCH 0
TO RIGHT HALF
OF SECONDARY
SWITCHES
A"
2
C5
SWITCH 0
LINE * TO OTHER
JUNCTORS INCOMING —
SWITCH 0 LINK FRAME
O
£
9
1-j $
9 TOOT
LINE
LIW
FRAMf
9,
9
81
0
L
R
0
L
R
9
o
\
\
o
INCON
LINK
,
0 .
9 ,
0 <
9
0
9
0 ,
9 ,
iO j
,9
\
0 19,
— »•
ING
— »
•• -•>
— >
^TO1'
RIGHT
OFPRI
swrro
HALF"
MARY
HES
HER
=S
LINE
LINKS
10 DISTRICT
JUNCTORS
«_ LINE
JUNCTOR
20S
UBSCRIE
LINES
iER
vj_ ' ,
TO RIGHT HALF
OF SECONDARY
SWITCHES
*'
LINE _? TO OTHER
JUNCTORS INCOMING —
LINK FRAME
FIG. 31. Double Primary-secondary Trunking Arrangement — Crossbar System (Courtesy Bell System)
the secondary switches of all the line link frames in the office. There will be at least one
junctor from each secondary switch on an incoming link frame to a secondary switch on
every line link frame in the office, or a minimum of 10 line junctor paths between any in-
coming link frame and any line link frame, the number of paths varying, depending on the
number of frames required in an office.
The line junctors on the verticals of each of the line link frame secondary switches have
access to 10 line links on the horizontal paths. The 10 line links are distributed over the
primary switches of the line link frame, one to each switch, giving each link access to the
called subscriber lines appearing on the verticals of the primary switch with which the
link is associated.
With the Fig. 31 arrangement of switches and the three groups of interconnecting link
paths, any incoming trunk can be connected to any called line appearing on the line link
frame or, by means of other groups of line junctors, to a called line on any other line link
frame in the office. This trunking arrangement is also employed for connecting district
junctors to outgoing trunks in the originating office.
Establishing a call from one crossbar subscriber to another crossbar subscriber requires
four stages of operation, two at the originating and two at the terminating office:
1. The calling subscriber is connected to a subscriber sender through the line link frame,
district junctor, and sender link frame, and the sender registers the dial pulses of the called
number.
2. The subscriber sender is connected to an originating marker through the marker
connector, and the marker then selects the switch frames for establishing a connection be-
tween the calling subscriber line and an outgoing trunk.
3. The outgoing trunk (uicoming at the terminating office) is connected to a terminating
sender through the terminating sender link frame, and the sender registers the pulses cor-
responding to the called number.
MECHANICAL SYSTEMS AND OPERATION
17-33
4. The terminating sender is connected to a terminating marker through a marker con-
nector, and the marker then selects the switch frames for establishing the connection to
the called subscriber line.
Future developments in crossbar equipment point toward simplification of equipment and
circuits and reductions in the number of units required, wherever possible. An improved
system of crossbar is now under study, in which it may be possible to establish connections
with one marker instead of the two markers now used, and in which other simplifications
may be secured.
OTHER RELAY SWITCHING SYSTEMS developed by various manufacturing
companies include Relaymatic, by Kellogg Switchboard and Supply Co.; Relaydial, by
Stromberg-Carlson Co.; All-Relay, by North Electric Manufacturing Co.
These systems operate on the principle of (1) finding the calling line when the calling
subscriber takes his handset from the hook, (2) selecting and closing groups of contacts
by relay action under control of dial pulses, subdividing the groups of contacts closed,
until the contacts of the called line are reached, after which ringing power is applied to the
called line by a link circuit. Since no moving parts are involved except the operating
springs or reeds, which are equipped with precious-metal twin contacts, maintenance is
simplified and operating costs are reduced over other types of automatic switching employ-
ing motors and step-by-step type switches with base-metal contacts and sliding brushes.
The line circuits may be assigned for common-battery local and rural, trunk or pay
station service. Local lines may have individual stations or multiparty service up to
10-party selective (for metallic lines) or 16- to 20-party code ringing (for grounded lines).
Local lines are of the metallic type, and line adapters are used for grounded rural lines, as
required. By the addition of a trunk adapter, any line circuit may be converted to a trunk
circuit. All link (connector) circuits have access to all lines, are assigned in rotation, and
automatically release from any line
in trouble or as soon as the subscrib-
ers hang up. A line lockout feature
is generally provided with these sys-
tems which prevents tie-up of a link
equipment if a line is in trouble or a
handset is left off the hook or if the
link fails to release after a predeter-
mined time. As soon as the line in
trouble is restored to normal, the
lockout of the line from access to the
link circuits is automatically discon-
tinued.
These systems are made in capaci-
ties from 10 to 10,000 lines and may
be operated as unattended small dial
offices, if desired, with trunks to a
nearby manual or mechanical office.
In such cases, suitable alarms are
provided which indicate at the at-
tended office when the equipment
needs attention and the type of
trouble at the unattended office.
Some systems of more than 200 lines
employ relay-type selectors to dis-
tribute calls from one group of 100
line finders to the desired 100-Hne
group of connector links and con-
nectors.
McBerty Automatic Telephone
System (North Electric Manufactur-
ing Co.). The important unit of
this system is the McBerty relay,
Fig. 32, a new design consisting of
an integral reed spring-armature-contact structure having no pivots or hinges, which are
common to most relays. The basic mounting structure may be used as a single multi-
contact relay or as a group of three, four, or five separate relays, the entire unit being
light and compact. The relay coils are of the molded bobbin, type, which slip over the
steel-alloy cores welded to the mounting frame. Gold-alloy contacts are used throughout.
Bare wire is used for multipling relay contacts.
FIG. 32. McBerty Relay (Courtesy North Electric Mfg.
Co.)
17-34
TELEPHONY
This system employs a link circuit consisting of a line finder, connector control relays,
and a connector for establishing a connection between a calling and called subscriber. As
many links are provided as are required to handle normal traffic loads. Figure 33 shows
a single link circuit layout for a 100-line system, but for purposes of illustration only
three of the ten tens relays are shown. Also for clarity each single line shown represents
two wires outside of and three wires within the switchboard.
When a calling subscriber removes his handset from the hook, the line relay in his line
circuit operates, causing the proper line finder tens and units relays of an idle link circuit
to operate, closing the calling line through to the connector control relays of this link.
The calling subscriber then dials the called number, and the dial pulses are registered by
LINES
LINE -FINDER <1,WF1 CW<!) CONNECTOR
UNITS RELAYS
PIG. 33. Diagram of North 100-line All-relay System (Courtesy North Electric Mfg. Co.)
the control relays. These relays cause operation of the connector tens and units relays
(corresponding to the called number) connecting the called line to this link.
The above operations complete the connection between the calling and called subscribers
through the link circuit, which applies ringing power to the called line. This link is not
released for other connections until the subscribers hang up. While the tens relays close
through ten lines in both the line finder and connector each time they are operated, only
one units relay is closed through in each line finder and connector for a given caU, and thus
all lines except the calling and called lines remain open to the control relays and may be
seized by other links when calls are originated by such lines.
The XY dial telephone system, developed by Stromberg-Carlson Co., employs for its
basic unit the XY selector-type switch, a view of which is shown in Fig. 34.
The XY switch, used in the line finder, selector, and connector circuits is radically
different in construction from the Strowger step-by-step switch. The switch is assembled
on a metal base plate, which is mounted horizontally on a switch frame. The switch has
a carnage with four separate wipers, tip, ring, sleeve, and hunt, and the carriage is moved
as a unit in two horizontal directions, one paralleling the front edge of the base plate called
the X direction, and the other at right angles to the X direction, called the Y direction
under control of two magnets, X and Y respectively. The carriage is driven by a cog roUer
(tubular shaft) assembly, which slides along a shaft during the X motion and rotates dur-
ing the Y motion. The cog roller is a double-cut tubular gear, with ratchet teeth cut par-
allel to its length and rack teeth cut as rings. The annular rack teeth mesh with and are
MECHANICAL SYSTEMS AND OPERATION
17-35
driven in the X direction by a sprocket actuated by the X magnet. The Y magnet ac-
tuates a pawl which engages the ratchet teeth of the cog roller, turning it around the
shaft.
Since the switch is 100 point, the X motion is given 10 steps (plus one for overtravel)
and the Y motion 10 steps (plus one for overtravel), thus providing for selection of any
one of 100 lines. Since four wipers are involved and each wiper has its own set of 11 wire
banks (each 11 wires deep), 44 rows of wires are lined up in front of the wipers. An X
wiper is also provided, which is operated by a pinion and rack assembly actuated by the
X magnet and which has access to a 23-wire bank to mark the level of X travel.
When the X wiper finds the proper level, thus positioning the wipers, on the carriage,
before the proper wire banks, the X magnet is de-energized and the Y magnet, assuming
control, moves the wipers into the wire banks until the proper line wires are reached.
Carriage
Sleeve
and-
Hunt
-^-Mechanism
Plate
X Magnet
•Y Magnet
•Release
Magnet
FIG. 34. The XY Switch (Courtesy Stromberg-Carlson Co.)
A number of unique features are built into the XY switch assembly, such as bare wire
multiple for line terminations, a new mechanical design for magnet current interruptions
to avoid armature chatter, and flexibility to function as a line finder, selector, or con-
nector; the fact that the common wire banks need be wired only once, for up to 50 switches,
results in large wiring economies.
The system requires line finders, selectors, and connectors, as in other step-by-step
systems, but the XY switch functions for each of these three units.
In operation, the calling subscriber removes his handset from the hook, thereby causing
his line relay to operate and an idle line finder, which is permanently associated with a
selector, to find and connect to the calling line. The calling line is thus extended through
to a selector which returns dial tone and supplies talking battery to the calling subscriber.
Assuming that the called number is 234, the first digit dialed is 2, which causes the selector
to move two steps in the X direction and into its wire bank automatically in the Y direc-
tion until an idle connector serving the 200 group of lines is found. When the second
digit, 3, is received by the connector, it moves its wipers three steps in the X direction, and
when the third digit, 4, is received, these wipers move into the wire banks in the Y direc-
tion to the fourth wire, thus connecting the calling to the called line. This connection is
not completed, however, until the connector applies ringing power to the called line and
the called subscriber has answered.
17-36 TELEPHONY
3. TOLL SYSTEMS AND OPERATION
Toll systems, as distinguished from local systems, are designed to handle toll traffic
over toll circuits. Toll traffic differs very materially from local traffic, since toll circuits
may extend from one toll office to a nearby toll office or to an office in this country or in
almost any other country in the world, involving many thousands of miles of circuit.
ToH circuits must be of a grade suitable in all respects for the traffic they are required
to handle. For the very long circuits, expensive equipment and complex arrangements
are necessary to meet all requirements.
In the smaller offices the toll and local positions are identical or in the same lineup; the
same line and cord circuits may be used for both local and toll service. In the larger toll
centers, involving a number of toll circuit groups, separate manual toll boards are provided
for concentrating in one switchboard, for a given toll area or center, all the toll circuits
serving that area. Such switchboards require special circuits and auxiliary equipment for
properly recording, ticketing, timing, and supervising toll connections.
MANUAL TOLL SWITCHBOARDS now in use in large metropolitan centers provide
outward positions for outgoing toll calls, inward positions for incoming toll calls, and
through positions for toll calls switched through the board from one toll circuit to another,
or, if desired, toll positions may be designed to handle both inward and through toll calls.
One type of manual toll switchboard (Western Electric Co. No. 3C) now in use is
equipped to handle all types of manual toll switching and, in connection with step-by-step
offices, may be arranged to handle those local dial calls requiring the assistance of an
operator.
The functions of this particular type of board are (1) to establish outward toll con-
nections while holding the calling subscriber on the line (combined line and recording
[CLR] traffic) , or to establish connections later, if for any reason the call cannot be com-
pleted on the first attempt; (2) to connect inward toll calls to the called subscriber line
if in the local or tributary office area; (3) to interconnect toll circuits (through traffic)
upon request of a distant operator; and (4) to handle miscellaneous local calls.
Outgoing calls from local or tributary (small office, having toll connections to its larger
toll center office) offices reach the toll board over recording-completing trunks from local
manual or mechanical offices or over tributary toll circuits from tributary offices. Inward
calls reach the toll operator over toll circuits (between toll centers) and are completed to
the local called subscribers over toll switching trunks, either on. a straightforward basis
through manual B boards or by dialing or key pulsing over mechanical trunks through a
mechanical office.
This switchboard has nine jack panels and three operator positions, each equipped with
ten pairs of high-impedance toll cord circuits, per section, and by adding sufficient operator
positions to handle the traffic load as many toll and trunk circuits as required can be ter-
minated in the switchboard.
These boards are equipped with calculagraphs for stamping the tickets with the elapsed
time of calls for billing purposes, electric clocks, ticket conveyors, ticket holders and com-
partments, and many other auxiliary devices for handling toll traffic. Transmission gain
may be introduced in the toll circuits, as required, when the operator inserts the plug of
her cord circuit into the toll line jack. Idle circuits and circuits busy may both be in-
dicated by lamp signals, and automatic listening equipment may be provided at inward
positions for incoming plug-ended toll circuit operation.
MECHANICAL TOLL SWITCHBOARDS OR SYSTEMS have been in use for some
years in a number of comparatively small toll networks, the first systems being of the dial
or step-by-step type,
The step-by-step system of toll dialing, though useful and economical for a small group
of interconnected dial offices, presents sizable operating problems where intertoll dialing
is attempted over an extensive area involving a large number of intermediate offices.
The mechanical switching, of toll traffic requires that the digits dialed by a calling sub-
scriber or originating operator at a given office, to reach a particular subscriber in another
part of the country, must be different from the digits dialed to reach any other subscriber.
In step-by-step toll dialing offices, the originating toll office is reached by the subscriber
dialing zero (0), tributary offices by dialing the figure one (1), and two more digits are
generally required to select the proper outgoing toll or tributary circuit. Thus, when a
call is dialed through a number of step-by-step toll offices, three digits must be dialed for
each office passed through in addition to the digits required for the terminating office and
called subscriber line. This requirement results in a long series of dialed digits for a call
that passes through a number of intermediate offices. Figure 35 shows that 19 digits are
required for a call from Portsmouth, N. H., to Vinland, Kans., involving only four inter-
TOLL SYSTEMS AND OPERATION
17-37
mediate offices. Additional intermediate offices, in this connection, would increase the
digits to be dialed, so that not only would there be dela^" in ascertaining the proper codes
to dial in order to extend the call through the various intermediate offices, but also the
dialing of a long series of numbers would retard operating time, would hold expensive
facilities unnecessarily long, and would tend to increase operating errors. Also, if delays
PORTSMOUTH, BOSTON
N.H. 053
NEW YORK
062
ST. LOUtS
078
KANSAS CITY
O26
LAWRENCE
133
jf fl T
VINLAND, KAN.
1234
FIG. 35. Intertoll Dialing Scheme — Step by Step System (Courtesy Bell System)
were encountered in securing any intermediate link or if the called line ras busy, the
complete dialing process would have to be attempted again.
THE NO. 4 CROSSBAR TOLL SYSTEM, a development of the Bell System, was first
placed in service in Philadelphia in August 1943. This system was developed primarily
to provide for ultimate toll dialing on a nationwide basis and was designed so that it could
be introduced gradually throughout the country on an economical basis without im-
mediately displacing existing manual or mechanical systems except as desired.
The No. 4 system is arranged, as shown in Fig. 36, to complete (1) outward calls from
local subscribers to outgoing toll lines, (2) inward calls from incoming dial or manual lines
\
TO DISTANT TOLL OFF
t
SUBSCRIBERS
TRAFFIC FROM SUBSCRIBERS IN PHILADELPHIA TOLL CENTER AREA TO OTHER TOLL AREAS
LOCAL
OFFICE
DSA OR OUTWARD
TOLL BOARD
CROSSBAR
EQUIPMENT
INCOMING DIAL TOLL LINE
-*•
INCOMING RINGDOWN OR
STRAIGHTFORWARD TOLL LINE
L±D
LOCAL
OFFICE
SUBSCRIBERS
LOCAL
OFFICE
SUBSCRIBERS
OPERATOR POSITION
(CONNECTED TO CONTROL
CROSSBAR EQU»PM€NT}
TRAFFIC TERMINATING IN PHILADELPHIA TOLL CENTER AREA
INCOMING DIAL TOLL LINE
OUTGOING DIAL OR
RJNGDOWN TOLL LINE
STRAIGHTFORWARD TOLL
LINE
_ OUTGOING DIAL OR
1
RI NGDOWN TOLL LI N E
C±3
CROSSBAR
EQUIPMENT
OPERATOR POSITION
(CONNECTED TO CONTROL
CROSSBAR EQUIPMENT)
INCOMfNG TRAFFIC SWITCHED AT PHILADELPHIA TO ANOTHER TOLL LINE
FIG. 36. Types of Calls Handled by the Crossbar System (Courtesy Bell System)
to local subscribers, (3) through calls between incoming and outgoing dial or manual toll
lines.
Outward calls, and incoming calls from toll lines equipped for toll-line dialing, are
automatically switched under control of dials or keysets at the originating end of the lines.
17-38
TELEPHONY
Incoming calls from other types of toll lines (ringdown or straightforward) are routed to
operator positions.
In the No. 4 system, crossbar switches with senders and markers are used in the same
general way as in the local crossbar system, with such variations as are required for toll
traffic. The operator positions which supplement the mechanical switching system for
handling terminating and through calls from toll lines not equipped for toll-line dialing
are of the cordless type, but cord positions may also be used to facilitate handling calls
over congested toll-line groups. This system permits toll-line dialing into a city having
panel or crossbar offices.
Figure 37 shows a block schematic of the main circuit components of the No. 4 crossbar
system. Five types of senders which act as automatic operators are provided, three for in-
coming and two for outgoing trunks. For each incoming call, an incoming sender is con-
nected, and, unless the call is to be completed over a manual trunk or one equipped to
receive multifrequency pulsing at the distant end (in which case only an incoming sender
is required) , an outgoing sender is also connected, as shown in Fig. 37. When an outgoing
FIG. 37. Block Schematic of Main Circuit Components of the No. 4 Crossbar Toll System (Courtesy
Bell System)
sender is used, the incoming sender transfers, through the primary and secondary frames,
all the digits received except the first three, which are used by the marker to control the
connection within the office. Incoming senders are designed to transmit d-c key pulses
and outgoing senders to receive them, the transfer of digits being at the rate of 8 per sec.
All incoming senders are also arranged to send out multifrequency pulses, so that out-
going senders are not required when the terminating points have senders capable of re-
ceiving this type of pulse, such as at local and toll crossbar offices. Ultimately, when
multifrequency pulsing becomes general, outgoing senders may be eliminated. While
incoming senders are arranged to send either d-c or multifrequency pulses, the dial in-
coming sender is designed to receive dial pulses (10 or 20 per second) recorded on crossbar
switches, and the key pulsing incoming sender to receive d-c or multifrequency pulses, as
may be indicated by a signal from the incoming circuit, as recorded on relays, four relays
for each digit. The third type of incoming sender (position) is associated with each oper-
ator's position; on an outgoing call from the position, the sender connects to a marker,
into ^ which it passes the first three digits received, for the purpose of establishing con-
nection to the desired outgoing trunk. When this trunk is selected an outgoing sender is
attached, except when the trunk is on the manual or multifrequency basis.
_ Both types of outgoing senders receive d-c key pulses, but each type sends out different
signals, depending on the signal the sender receives from the outgoing trunk. One type
receives four or five digits and controls the sending of either revertive or call-indicator
pulses. Revertive pulses are used for completing calls to panel or crossbar offices; call-
indicator pulses, for calls to manual offices in panel areas. The other type of outgoing
sender receives up to 11 digits, and either sends them out as dial pulses into a step-by-step
TOLL SYSTEMS AND OPERATION
17-39
office or connects itself to a call-announcer and controls the sending of the latter's voice
announcements, which are limited to five digits,
Figure 38 shows the types of connections that incoming and outgoing senders are re-
quired to control. For a call to a local office within the crossbar toll office area, only the
called office code and four or five digits are required to reach the subscriber from the cross-
bar toll office, since the trunk selected by the crossbar equipment connects directly with
the called office. For a call to another switching area through an intermediate point,
one, two, or three additional digits for use at the intermediate point must be dialed or
keyed following the switching code, requiring up to 14 digits maximum.
All senders are safeguarded from being held too long on a connection by timing circuits,
which, after a predetermined time, signal the originating operator to start the call again,
and are then released. When trouble involving the sender exists, the sender is auto-
matically held for inspection and the maintenance forces are notified by alarm circuits.
ORI
<
G1NATI
OFFICE
IMG
h
8
11
JO. 4 TOLL
5
TQ
=U^4AT
OFFICE
ING
Cf
STE
^R
M-
— r
5
Cl
STE
PANEL
it
8
PANEL
y
X
*OSSBX
.
SOSSBAR
V
^
AORTC
SWITCH B<
(DIAL OR
PULSING
MANU
>LL
DARD
KEY
, OR
AL)
\
8 TOLL
SWITCHING
POINTS
/"
P BY STEP
P EOT STEP
^ 5
MAMUAL
NOTE: NUMBERS ON THE LIMES INDICATE THE MAXIMUM NUMBER OF
DKSITS TRANSMITTED
FIG. 38. Representative Types of Calls Switched by the No. 4 Crossbar Toll Office (Courtesy Bell
System)
TELEPHONE REPEATERS are essentially voice-frequency amplifying devices with
suitable talking and monitoring features designed for use in voice-frequency toll circuits
which would, without amplification, be greatly restricted in their length. By means of
such devices, properly spaced and controlled, toll circuits may be extended to any prac-
tical length desired.
In the early designs, telephone repeaters were basically of two types, those in the Bell
System being designated 22-type for two-wire circuits and 44-type for four-wire circuits.
Present Bell System practices employ a single type of amplifying device for either two-
or four-wire circuits, and suitable connecting arrangements to connect it into the two- or
four-wire circuits or any combination of such circuits.
Figure 39 (a) and (&) shows a schematic diagram of the two- and four-wire arrange-
ments, respectively. "Where a repeater is employed at the junction of a two- and a four-
wire circuit, the two-wire arrangement is used for connection of the repeater to the two-
wire circuit and the four-wire arrangement for connection of the repeater to the four-wire
circuit.
In the two-wire arrangement, the separate branches of the amplifiers are joined electrically
through repeating coti hybrids for a repeater at an intermediate point in the telephone cir-
cuit. For a repeater at the terminal of a circuit a resistance hybrid arrangement (see Fig.
39[c]) usually takes the place of the repeating coil hybrid on the switchboard (drop) side
of the repeater. In the four-wire arrangement repeating coil hybrids are not usedt except
where required at the junction of two- and four-wire circuits. Four-wire terminating
sets are employed on the drop side of four-wire repeaters.
The repeating coil hybrid arrangement (Fig. 39(a]) consists of two repeating coils, A
and B, with low-inductance windings so related and connected as to form, with associated
equipment and the line, a balanced bridge circuit when the line and balancing equipment
impedances are equal and the impedances connected to terminals 2-5 of each coil are equal.
Coils of different ratios to match various line circuit impedances, and with phantom cir-
cuit taps for securing a phantom circuit, if desired, are available.
17-40
TELEPHONY
x LIINt
REGULA1
HERE
tuui^iv
ING N
IF REC
-JjL_
. J.
ItNl *!*•--_ .1
ETWORK
2UIRED)
B
1
BALANCING
A EQUIPMENT
EG
12
BA
EG
—
ro
0
X
>E*-~Jr
.cRv.jr J
•JW^-
6 5
^J^"
FILTER
— fr— 0 )( i )(
)( | X -0—0
>
)( i X ' 0- 0
^TO^.
5 6
-nft$^-
-nm^--
II 12
10 9
sWT\-
siffl^-
3 4
8 7
y-5^5%..
LANCIts
IU1PME
JG
NIT
•'TOr*-
9 10
s$W*
•nfflp-
4 3
7 8
^W^
[
REPEATING COIL
^ HYBRID
/7KRTk-
•aR^
^RT^-
4 3
/-tfffif^
T
LOW-
FREQUENCY
EQUIPMENT
T
LOW-
FREQUENCY
EQUIPMENT
./fflffiX
10 9
II 12
••^TO^-
/^?or?cv
LINE
4
J
-•» OOu *•
8 7
./^^
-^TO5^
5 6
2 1
./TO\.
TO LINE
J^ EQUAL-
CROSS
JACKS
A
^TO5
6
t
KW
•\
5
2
TO!
PHANTOM
iTO ' '
PHANTOM
0—0 X ' X
<
0— — 0 )( I K
X i X 0- — 0—
1 FILTEF
xi
"~1T-
^ j
— 4 —
CONNECTIONS
B
REGULATING NETWORK
HERE(F REQUIRED)
(a)
' ^«ev« • OUTPUT
-INPUT LINE EQUIPMENT *]* 1/2 OF VI .^ UNE EQUIPMENT—*.
TO PHANTOM
"!
R
SPEATE
R
REGU-
LATING
NET-
WORK
-0*-X»<"
-*•
•*•
t>
•K-'
•M-
-HO-
•?eO"
Tf
> PM
AMPLIFIER
KM v:
•> r
EQUIPMENT
IN
: v AMT •
-r {(
RU
A
U l
A A A
i? ii^
V
A A A
U
LINE—,
BUILDING-1-
OUT "
CONDENSER
I/
TO
=; DROP
CIRCUIT
A
A A A
T™ T2^ | *~
AAA
9 Vvv*
_ n v «.
~ vvv -- |^ »
EQUIPMENT
OUT 'HrvDi
* AMPLIFIER? !^DT
IN i (C)
RMv:
RH A.
1
r\ y
FIG. 39. Terminating Arrangements used with Telephone Repeaters (Courtesy Bell System)
TOLL SYSTEMS AND OPERATION 17-41
Incoming current from the line flows through, the line windings of both coils and induces
equal voltages in the network windings 9-10-11-12 of both coils. Since the poling of the
network windings of coil A are reversed with respect to the network windings of coil B,
the resultant voltage across the network (balancing equipment) is zero. The voltages
induced in the 2-1-6-5 windings of both coils are likewise equal, and the power received
from the line (deducting coil losses) divides equally between the impedances of the ampli-
fier branches connected to 2-5 of each coil. Since these branches transmit in opposite
directions, the power received from the line from a given direction by one of the branches
and its amplifier is effective, while that received by the other branch and its amplifier is
ineffective.
Outgoing current from the effective amplifier flows through the 2-1-6-5 winding of coil
B and induces equal voltages in the line and network windings of coil B. The result-
ing currents in these windings also flow through the corresponding windings of coil A to
the line and balancing equipment, respectively. The currents in the line and network
windings of coil A induce equal voltages in the 2-1-6-5 winding of coil A, but these volt-
ages are opposing in phase because of the reversed poling of the network windings, and
the resultant voltage is zero. The power received from the amplifier (deducting coil
losses) thus divides equally between the line and the balancing equipment. The power
received by the line is useful, while that absorbed by the balancing equipment is wasted.
In order to secure a satisfactory trans-hybrid balance, the windings of a given coil must
be mutually balanced to a high degree of precision, but separate coils need not be so highly
balanced with respect to each other.
The resistance hybrid arrangement (Fig. 39[c]) is composed of resistances, condensers,
and the necessary terminating jacks connected to form a four-branch balanced lattice
type network. This network joins together the amplifier branches on the terminating
(drop) side of the repeater and terminates them in the required 600-ohm two-wire drop.
The network presents a 600-ohm impedance in all four directions. The 1000-cycle loss
through this network is 10.7 db for each direction of transmission.
In the four-wire arrangement, one-half of an amplifier unit is employed in each side of
the four-wire circuit, transmitting in one direction only. Single repeating coils, of the
type used with two-wire arrangements, are provided to match the impedances of the line
and amplifier. Phantom taps are provided in these coils, and the coils must be matched
for balance when phantom circuits are employed.
The amplifier circuit of the repeater is shown in Fig. 40. This circuit has a nominal input
impedance of 600 ohms, and the input transformer impedance ratio (windings 9-8 to 1-7)
is 300 to 357,000 ohms. The output transformer has four windings, of which winding
9-10 is for the negative feedback feature. The output impedance ratio of this trans-
former (windings 7-S to 1-2) is 21,000 to 600 ohms.
The amplifier vacuum tubes are heater-type pentodes, 310 A for regulated and 328 A for
non-regulated battery supply.
Grid bias on the tubes is obtained from the voltage drop in resistances B and C and in
the potentiometer through which the total cathode current flows.
The total gain of each amplifier is about 35 db; the secondary winding of the input
transformer is tapped to provide a total gain adjustment of 20 db in 4-db steps; and the
potentiometer serves as an additional gain control with a range of about 5.4 db. The
power-carrying capacity of the amplifier is such that the transmission level at the amp out
jacks may be as high as + 10 db with respect to the transmitting switchboard. The nom-
inal d-c battery supply is 24 volts for the filamenib current and 130 volts for the plates.
Attenuation equalizers for two-wire repeaters are associated with the line equipments
and are connected to the amplifier inputs at intermediate repeaters and to the receiving
amplifier line input at terminal repeaters (terminals 1-6 and 2-5 of coils A, Fig. 39[a]).
They are of the fixed type and designed for repeater sections of average length. The
low-frequency equalizer for equalization in the low-frequency range consists of capacitance
or a combination of capacitance and resistance, depending on the line characteristics.
At two-wire circuit terminals, this equalizer is omitted in the transmitting side of the
terminal repeater. High-frequency equalization on two-wire circuits is obtained by tbe
effects of the various equalizer units mentioned and by interaction effects between the
filter and the impedances between which it is inserted.
Equalization for four-wire circuits (see Fig. 39[5]) is provided by a low-frequency equalizer
consisting of a condenser shunted by a resistance, and a high-frequency equalizer consisting
of a combination of resistance, inductance, and capacity.
Low-pass filters of nominal 600-ohm impedance are provided, to limit currents above
the voice range to be transmitted, in the four-wire branches of the line equipment, as-
sociated with the amplifier input for the two-wire arrangement, as shown in Fig. 39{<z),
Three types of filters are provided, having nominal circuit cutoffs of 2450, 2850, and 3500
17-42
TELEPHONY
cycles per second. The filter is omitted from the transmitting branch of terminal re-
peaters.
Regulating network equipment is provided for insertion in the repeater circuits (see
Fig. 39[a] and [6]), as required, to compensate for changes in line attenuation due to
temperature variations. This equipment functions under control of a pilot wire regulating
system which actuates relays, causing resistance-type loss pads to be cut in or out of the
repeater circuit, as required, to maintain circuit transmission levels. This equipment is
more fully described in another part of this section.
ODD AMPLIFIER CIRCUIT
PLATE
FIG. 40.
EVEN AMPLIFIER CIRCUIT
VI Telephone Repeater Circuit (Courtesy Bell System)
The balancing equipment, connected to 9-12 of each A coil (Fig. 39[a]), is required to
balance the line and its equipment (up to the repeating coil hybrid) in each direction of
transmission for two-wire arrangements but is not required for four-wire arrangements,
at intermediate points. At both the two- and four-wire terminal repeaters, a simple
compromise network is employed on the drop side with the resistance hybrid (Fig. 39 [c])
and four-wire terminating sets, respectively. Balancing equipments are designed in
various combinations of resistance, capacitance, and inductance to closely match the
impedance of their various associated lines.
Signaling over repeater-equipped circuits requires the use of auxiliary signaling circuits
employing 20, 135, or 1000 cycles or composited d-c signaling on two-wire circuits. The
20- and 135-cycle and composited d-c signals are by-passed around intermediate re-
peaters, through which such signals will not pass, but 1000-cycle signaling will pass through
the repeaters in the same manner as voice-frequency currents. For four-wire circuits,
in which there are usually a number of repeaters, 1000-cycle signaling is generally employed
as the most economical and satisfactory arrangement.
TOLL SYSTEMS AND OPERATION
17-43
CARRIER TELEPHONE SYSTEMS permit the securing of additional telephone chan-
nels between two toll centers by superimposing carrier frequencies on voice-frequency
wire circuits between these points. At the terminals of the carrier channels, carrier equip-
ment is required _ which is capable of converting voice frequencies to modulated carrier
currents, transmitting them over the wire circuit, and reconverting or demodulating
them at the receiving end to voice frequencies. This equipment must operate in both
directions of transmission. Carrier equipments (carrier repeater or transfer units) are
also employed for amplifying carrier currents and for transferring the carrier channels
where the wire circuit does not, but the carrier channels do, extend tnxough the inter-
mediate office.
Carrier telephone systems are in operation in many countries, but they are in use to the
greatest extent in the United States because of its vast network of toll circuits. These
systems are manufactured by a number of different companies, both Independent and
Bell, the number of two-way channels provided in the various systems ranging from one
to twelve, excluding the L-type carrier system. The Bell System is the largest manu-
TYPE OF
SYSTEM
CA
CS
CT
cu
D
CARRIERS
[1](T|[3[ 9.3 12.4 15.9 22.5 26.2 3O.2
E TO W W TO &
9.3 12.4 15.9 19.5 23.2 27.2
7.6 10.6 13-9 16.6 19.8 23.7
6.3 9.4 12.9 20.7 24.4 28>*
6.3 9.4 12.9 19.8 23.7 27.7
tZ] LOWS? SIDE BAND
tZ3 UPPER SIDE BAND
E TO W W( TO E
lulu to tutotii
E JO W W TO I;
60 70 80 90 XX>
FREQUENCY W K1LX>CYCLES PER SCCONO-
FIG. 41. Channel Frequency Allocations for Telephone Carrier Systems (Courtesy Bell System)
facturer and user of carrier telephone equipment in this country, and the frequency al-
location chart shown in Fig. 41 applies to carrier systems of Western Electric Co. (Bell
System) make. From this figure, it is seen that the D, G, and H systems provide a single
channel, the C series three channels and the J and El systems twelve channels, all two-
way.
In operation, the basic principle is the same, regardless of the type of system or the
number of channels provided. Figure 42 shows a block schematic of a type C carrier tele-
phone system with one intermediate carrier repeater.
It will be noted that each of the three channels has identical equipment units at both
the east and west terminals, and that identical common equipment is provided at each
terminal to serve each of the three channels. The carrier repeater also serves all three
channels. Voice-frequency transmission over the wire circuit is not interfered with by,
nor does it interfere with, the carrier currents, because of the low-pass and high-pass filters
associated with the wire line at each terminal and at the repeater or transfer points. The
low-pass filter will pass only voice and the high-pass filter only carrier frequencies.
17-44
TELEPHONY
a
£
It!
Be loci
£<5 |S«S|
S.a. o * ±
fll l|a
ffi
LL
J_i L_
si
1
f
1
I
1
1
1
1
§
O
•a
.2
I O
O
TOLL SYSTEMS AND OPERATION 17-45
Incoming voice frequencies (about 250-2750 cycles) into channel 1 (Pig. 42) at the west
terminal pass to the modulator, where they modulate a carrier frequency. The lower
sideband only (assuming this system is of the CS type) is transmitted through the band
filter, transmitting amplifier, and directional and high-pass filters to the wire line. At
the intermediate point the sideband frequencies pass through the high-pass and direc-
tional filters, equalizer, west to east amplifier, directional and high-pass filters, thence
to the line. At the east terminal the sideband passes through the high-pass and directional
filters, receiving amplifier, band filter, and demodulator to the voice terminal of channel
1. Transmission takes place similarly in the opposite direction. The band filters pass
only the band of frequencies intended for their particular channels, blocking out all fre-
quencies of other channels which travel the common paths. The directional filters sep-
arate the incoming and outgoing bands of frequencies. The amplifiers, which are of the
high-gain, negative-feedback type, are necessary to maintain proper levels of transmission
for the carrier currents. The pilot equipment indicates and controls the transmission
levels automatically, so that manual adjustments are not required. The three-winding
transformers (hybrid coils) separate the transmitting and receiving voice paths at the
voice-frequency terminals of each carrier channel.
For open-wire operation, present practices make use of the G system for single-channel
very short circuits (under about 25 miles) , the H system for single-channel medium-length
circuits (up to about 300 miles, with repeaters about every 125 miles) , and the C system
for three-channel groups ranging from about 100 miles to any length desired with re-
peaters about every 150 miles. The G system equipment does not have an amplifier,
but one may be associated with the system externally. The CN allocation of the type
C system and the D system are not used for new installations. All these systems are con-
sidered to be in the low-frequency group of carrier systems (up to about 30 ke), and they
provide about 2500-cycle voice bands.
The broad-band carrier systems operate in a range from about 12 to 2000 kc or more and
provide about 3000-cycle voice bands. As may be noted in Fig. 41, the K system, for
toll cable use, functions between 12 and 60 kc; the J system, for open wire, between 36
and 140 kc; and the L system (not shown), for coaxial cable use only, between 60 and 2000
or more kc. The J and K systems may be operated any distance desired but require re-
peaters about every 70 and 16 miles respectively.
The L type carrier system, operating over specially designed conductors, known as
coaxial cable, because of their construction, is capable of providing up to 480 two-way
circuits per pair of coaxials (depending on the make-up of the cable) if coaxial amplifiers
are spaced about 5 to 8 miles apart. Practically, however, the number of circuits to be
provided in any L system will depend upon traffic requirements, since circuits can be added
as desired at any time in groups of 12.
Figure 43 shows the frequency translations which take place at an L type carrier tele-
phone system terminal. Three steps of modulation are employed to change an individual
voice-frequency channel of 0 to 4 kc to its proper line frequency assignment. The first
step of modulation occurs in the channel bank and translates a group of 12 voice channels
to the 60 to 108 kc frequency band. The second step of modulation occurs in the group
modulators and moves each fundamental group of 12 channels each (60 to 108 kc) to one
of five frequency assignments (each 48 kc wide) within the 312 to 552 ke band. This
band, designated a basic supergroup, is 240 kc wide and accommodates 60 channels of 4
kc each. The third step of modulation occurs in the supergroup modulators and translates
each basic supergroup of 60 channels each (312 to 552 ke) to one of eight frequency as-
signments (each 240 kc wide) within the 68 to 2044 kc band. The 480 voice-frequency
channels take line frequency positions within the 68 to 2044 kc band, and the four pilot
channels are assigned to frequencies of 64, 556, 2064, and 3096 kc. The supergroups are
separated by 8 kc each, except that 4 kc and 12 kc separate the first and second supergroups
and the second and third supergroups, respectively.
All long-haul carrier systems, including the C, JT K and L systems, have regulating and
pilot channel equipment which automatically adds transmission gain or loss as is neces-
sary to maintain the channels within predetermined transmission equivalents. For
cable facilities the normal transmission changes are due to temperature variations, being
greater in aerial than in underground cable. Flat gain regulators with master controllers
are employed in every repeater section for K systems. However, the amount of at-
tenuation variation in cable pairs with a given change in temperature is not the same for
all frequencies, an effect known as twist. To overcome twist effects, correcting circuits
are also provided about every 100 miles for aerial and 200 miles for underground cable.
Large economies are possible with carrier systems, principally to provide additional
toll circuits between toll centers. Their usage avoids, in many cases, the stringing of ex-
17-46
TELEPHONY
pensive wire circuits or possibly building a new pole line for open wire or cable or placing
underground cable. In any event, studies will indicate the economies involved.
The basic 12-channel equipment units of the J, K, and L systems are similar, the channel
modulators elevating the voice-frequency bands for 12 channels (4 kc per channel) from
0-48 kc up to 60-108 kc for these systems. Similarly the channel demodulator receives
the 12 channels at 60 to 108 kc. The K system operates over separate toll cable pairs in
separate cables with carrier repeaters, using the 12 to 60 kc band in each direction in the
CARRIER
FREQUENCIES
OF — *3096 PILOT
SUPERGROUP -»>2064 PILOT
MOTES:
U- CHANNELS ARE UPPER
SIDEBANDS
L- CHANNELS ARE LOWER
SIDEBANDS
FREQUENCIES ARE IN KILO-
CYCLES PER SECOND
MODULATORS |-p
JlJ 1556
BASIC
SUPERGROUP
OF 60
CHANNELS,
CARRIER I
FREQUENCIES \
OF GROUP {
.MODULATORS,!
FUNDAMENTAL
GROUP OF 12
CHANNELS
LOWER
.SIDEBANDS ,
Y
12 CIRCUITS *
612 -»
564-»
516 -»
468-*
420 -»•
_5_
~Z-
\
k
552
504
456 1
408f
360
312J
2044
1804
1796
T| 1052
-5j 812 §
804
8E
- 556 PILOT
LU312
— *• 64 PILOT
40 OF THESE MODULATED I
IN GROUPS OF 5 MAKING 8 OF THESE
FIG. 43. Frequency Translations at an L-type Carrier Telephone System Terminal (Courtesy Bell
System)
cables. The T system employs the same open-wire circuit in both directions, using line
frequencies of 36 to 84 kc west to east and 92 to 140 kc east to west. The L system em-
ploys two coaxial units for the two directions of transmission, hence the same frequency
band, from 60 to the required top kilocycle frequency, in each direction. Group frequency
modulators move 12-ehannel groups from one frequency range to another, as required.
Figure 44 shows a block schematic of a type J carrier telephone terminal; Fig. 45, a
type K carrier telephone terminal in more detail; and Fig. 46 a, frequency translation di-
agram for the type J system.
The particular range of frequencies, 60 to 108 kc, to which the voice frequencies are first
elevated in the J, K, and L systems was chosen, because (1) high-grade crystal niters can
be most economically built for operation in this general range, (2) the second harmonic
(120 ke> of the lowest frequency (60 kc) lies well above the highest frequency (108 kc),
precluding the possibility of interference between the second harmonic (from any channel)'
and other channels, and (3) manufacturing economies are achieved by using the same
TOLL SYSTEMS AND OPERATION
17-47
17-48
TELEPHONY
13S ^V^JIWH31
TANDEM SYSTEMS AND OPERATION
17-49
500
. **-^ 2
-i i -I s
WEST- EAST
FIG. 46. Frequency Translations in Type 3 Carrier Systems (Courtesy Bell System)
group of channel carrier frequencies for all the broad-band systems. The line frequencies
12 to 60 kc were chosen for the K system because, for non-loaded cable pairs Goading not
being available for these frequencies), the attenuation increases with frequency and in the
frequency range chosen the attenuation-frequency increase is about uniform.
4. TANDEM SYSTEMS AND OPERATION
Local tandem offices are provided, usually one to each extensive multioffice area, where
a large number of offices are located within and adjacent to city boundaries. The tandem
office is generally centrally located to the offices it serves and has direct trunks to all these
offices and also to attended PBX (private branch exchange) switchboards having a number
of pay stations, to the toll board, and to various special service boards. It is neither
economical nor practical in large metropolitan centers to provide a group of outgoing and
a group of incoming direct trunks between each pair of offices in the center, since cable
plant and the terminating trunk equipments required would be too costly. For many
combinations of two offices some distance apart the traffic is usually so light as to preclude
the use of expensive cable pairs between them for trunk purposes. Thus, the tandem office
provides an economical means of trunknig calls in the larger centers because a common
trunk group is provided between each office served and tandem,
Although the introduction of a tandem office in the call trunHng system of a given area
adds another office to the system and may materially lengthen the trunk mileage between
certain pairs of offices, depending on the geographical location of the tandem office with
respect to the surrounding offices, it is evident that two groups of trunks (one outgoing and
one incoming) between each pair of offices in a large center of, say, 50 offices would result
in an uneconomical trunk network and equipment layout and a more complex arrangement
of handling traffic. Also, the greater number of calls handled by the tandem trunk groups
increases their efficiency and may largely offset the tandem layout costs. Tandem offices
are warranted, however, in any particular case only if a comprehensive study of all the
various factors involved indicates their need.
One system of tandem trunking now in use provides for trunMng from a local manual
office to a panel sender tandem office on a straightforward basis. The local A operator,
upon receiving a call, inserts the calling plug of an A cord circuit into an idle outgoing
trunk to tandem, causing selection to be made at the tandem office of an idle operator and
17-50
TELEPHONY
a tone to be sent back to the A operator indicating that the tandem operator is ready to
receive the call. The A operator passes the called office name and number over the trunk
to the tandem operator, who registers this information on a keyset (a unit composed of
individual keys having office code and number designations), with which each tandem
position is equipped. The operation of the keys in the keyset causes pulses or number
announcements to be sent out over the tandem to called office trunk, thus reaching the
called office.
If the called office is of the step-by-step, panel, or crossbar type, the incoming pulses from
tandem reach selector (in step-by-step) or sender equipment (panel or crossbar) in the
called office, which completes the connection to the called subscriber in the regular man-
ner, as previously described for these systems.
If the called office is of the manual type, the incoming pulses reach call announcer
equipment at the tandem office before passing out over the trunk where they are con-
verted from pulses to spoken numbers which reach an idle 3 operator's ear at the called
office; or, where call announcer equipment is not provided, the tandem sender equipment
sends out pulses over the trunk to call indicator equipment at the called office, which causes
the called number to be 'displayed before the B operator. In either case the B operator
connects the plug-ended trunk circuit over which the call is being routed into the called
subscriber multiple jack, and ringing automatically starts on the called line. Supervision
of the call at the local, tandem, and B boards is by means of the usual lamp signals.
If the calling subscriber is in a mechanical office (step-by-step, panel, or crossbar), the
call is usually routed to a special board in the calling office. The special operator passes
the call to tandem on a straightforward basis, and the connection is then completed by the
tandem operator in the same manner as described for a calling local manual office.
Crossbar tandem equipment is now standard for new tandem offices, rather than the
manual tandem arrangement, just described, where it is applicable. This equipment
handles calls over two-wire trunks from panel or crossbar offices to other panel, crossbar,
or panel indicator manual offices by means of crossbar switches in a marker system of
operation. Calls from a manual office through crossbar tandem would reach a tandem
operator over straightforward trunks and be completed as described for the panel sender
tandem office.
The major switching frames in crossbar tandem offices correspond somewhat to the
frames in a local crossbar office. Incoming trunks, terminated on incoming trunk frames,
connect through trunk link frames, an office junctor grouping frame, and office link frames
to outgoing trunks, which terminate in incoming trunk equipment in other offices as shown
in Fig. 47.
TERMINATING
OFFICE
ORIGINATING
OFFICE
T,R & SI
T, R & S1
T & R PANEL TANDEM USING
.. TRUNKS IN COMMON
WITH CROSSBAR TANDEM
MAIN
DISTRIBUTING
FRAME
FIG. 47. Crossbar Tandem Office Units — Crossbar System (Courtesy Bell System)
When a ^call reaches the tandem office incoming trunk equipment, tandem sender and
marker units are caused to associate with the trunk and li^Tr frames involved in the call.
The sender receives and registers the incoming pulses from the originating sender on a
revertive (pulses sent back) or dial pulse basis, and it controls the tandem switch selec-
tions and the selections in the called office. The marker which is associated with the
sender through the marker connector frame routes the call through the tandem equip-
ment under control of the tandem sender registrations.
COMMON SYSTEMS 17-51
5. AUXILIARY SERVICE EQUIPMENT
SERVICE OBSERVING DESKS are provided, where required, at individual offices or
at a central location for observing the performance of switchboard operators and switch-
ing equipment.
One type of service observing desk is intended primarily as a non-centralized observing
bureau for use with toll or local crossbar, step-by-step and manual, or combinations of toll
and local plant. This desk is generally employed where not more than one desk position
is required, and observations are confined to circuits at the same location as the desk.
This desk is equipped with a cord circuit, operator's telephone circuit, jacks, lamps, keys,
and other equipment for observing on lines and trunks.
For mechanically operated systems, pen registering equipment is also employed to re-
cord the subscriber dial and line registering pulses, as required.
Central observing desks require direct lines to the various offices which are to be ob-
served^and as many desk positions as necessary to make the desired observations.
The information obtained by means of these desks is a very important aid in improving
operator and equipment efficiency and in bettering service generally to the public.
INFORMATION DESKS are provided at individual offices or central locations to
furnish subscribers with information about telephone numbers not listed in the telephone
directory or changed from the directory listing and about many other items essential in
assisting the subscribers to secure a wholly satisfactory telephone service. Up-to-date
files of telephone listings are maintained at the information desks accessible to each in-
formation operator. Centralized information desks require that subscribers in each
office be routed over the trunMng system, provided for such service, to the centralized
desk. Individual office information desks are reached over direct intraoffice trunks.
CHIEF OPERATOR DESKS are, if required, located one in each office. Various types
of calls are referred to the chief operator, who is in direct charge of the operating forces.
Complaints from, the subscriber about the service rendered or any other items regarding
the wishes of the subscriber in connection with calls the handling of which is not the
operator's function are referred to the chief operator or a supervisor.
''• Trunks are provided from manual or DSA boards to the chief operator desks, over which
these calls are routed.
REPAIR SERVICE DESKS are required in all but the very small offices to receive
subscriber complaints of service or reports of trouble encountered with the substation
equipment or telephone plant in general. Many other types of reports from the public
are also referred to these desks, which are convenient contact points for subscribers. Rec-
ords are maintained of troubles reported and cleared on subscriber lines, and valuable data
are secured from them for studies of troubles and their elimination.
Repair trunks are provided at individual offices or to a central point for receiving these
calls except in small offices where such calls are usually received at local testboards.
6. COMMON SYSTEMS
MAIN DISTRIBUTING FRAMES (MDF) are required in central offices for terminat-
ing the outside local and toll lines, which are usually brought into the office on cable pairs.
These pairs terminate directly on protector strips, mounted vertically on the vertical side
(VMDF) of the frame. In the smaller offices local and toll MDF are usually combined;
in the larger installations, involving a number of toll and toll entrance cables, separate
local and toll frames are provided. Terminal strips with insulated ,metal terminals are
mounted horizontally in rows (shelves) on the horizontal side (HMDF) of the frame, and
these terminals are cabled to an intermediate distributing frame (IDF). Cross-connecting
wire (Jumpers) may be run between any vertical protector strip and any horizontal ter-
minal strip so that any incoming line on the VMDF may be connected to any pair of ter-
minals on the HMDF. Other arrangements of protector and terminal strips are also
used, depending on the needs of the individual office.
INTERMEDIATE DISTRIBUTING FRAMES (IDF) are usually employed in both
manual and mechanical offices for local and toll lines. These frames have terminal strips
on both the horizontal (HIDF) and the vertical sides (VTDF) of the frame. For manual
local lines cabling from the MDF is terminated on the HIDF terminal strips, to which
cahling from the manual A and B boards is also multipled. For small subscriber lamp
multiple and single office boards, the B board and its cabling are omitted. The subscriber
answering jacks in the A board and the line circuit equipment are cabled to the vertical
terminal strips (VIDF) . Cross-connecting wire may be run between any horizontal and
17-52
TELEPHONY
GROUNDED
any vertical terminal strip, thus providing a means of connecting any outside line to any
subscriber A. and B board multiple jack and to any answering jack and line circuit. By
properly distributing heavy and light calling lines throughout the switchboard, traffic loads
can be more uniformly spread over the operator positions.
Relay racks are also provided for mounting various types of apparatus, such as relays,
repeating coils, apparatus mounted on panels, testing equipment, and many other equip-
ment units.
PROTECTORS are provided at the vertical side of the MDF in all central offices having
exposed outside cable or open wire plant in order to protect the equipment from damage
due to excessive voltages and currents from foreign sources such as lightning and power
lines. Figure 48 shows a typical protector used at main frames. Where the outside cable
enters aerially and is exposed to these foreign sources, as it may be in small offices, fuses
are also required in the circuits, unless the
I CABLE CONDUCTORS enterm£ Cable haS at leaSt 6 f * °f ^ Or finer
\ TO OUTSIDE PLANT gaSe cable inserted in it in such manner that
no power line contacts can occur between
the point of insertion and the MDF.
The protector consists principally of a
spring assembly, arranged to hold two heat
coils and two sets of protector blocks, one of
each for each side of a metallic line. The
heat coils designed to protect delicate cen-
tral office equipment usually operate if 0.35
amp flows for 3 hours or longer or if 0.54
amp flows for more than 210 sec. This coil
consists of a small coil of wire wound around
JL IJI-Jl— • HEAT coiu a c°PPer tuke» into which is inserted a metal
I all T!" pm ^e^ *n p*ace ky easily melting solder.
I jlBfl ^ke c°il °f wi16 *s placed in series with the
wy 1 vW^K jjne conductor, and if sufficiently heated the
solder melts, releasing the metal pin, which
is forced against a grounding spring by the
outside line spring of the protector. Several
types of protectors and heat coils are avail-
able; some of the heat coils open the line
conductor when they operate and may be
TO CENTRAL
OFFICE EQUIPMENT
PROTECTOR BLOCKS
i_J ------- CARBON
L ----- L ------- PORCELAIN
FIG. 48. Main Frame Protector with Heat Coils
and Protector Blocks (Courtesy Bell System)
reset mechanically without replacing or
resoldering the coil. The protector blocks
consist of a porcelain block with carbon in-
sert and a solid carbon block, a pah- to each side of the line, the air gap between the insert
and carbon block being about 0.003 in. This gap will, on the average, break down at
about 350 volts potential.
The protector ground bars are bonded to a main-frame ground bar which is connected
to the office ground.
TESTBOARDS are provided in all attended central offices, and testing equipment of
suitable design in all offices, for the purpose of deterrnining the condition of lines and
equipment, either because of reported or indicated trouble or as a trouble-preventive
measure.
Many types of test cabinets and testboards have been made available to meet the needs
of the particular location in which they may be installed.
In small manual local offices test cabinets, equipped with voltmeter (with batteries),
test keys and cords', trunks, and in some cases an external Wheatstone bridge, are em-
ployed. In large manual installations a number of positions of testboard may be used,
depending on the volume of repair and subscriber installation work involved. Each of
these positions usually has a voltmeter, test keys and cords, trunks, and access to one
Wheatstone bridge, as required. Lines and equipment are tested on reports of trouble
or after installation work is completed, and, in case of trouble, its location is determined
and the trouble is cleared by outside repairmen.
In manual toll offices testboards (primary, secondary, or both) are arranged with a
group of jacks for each toll circuit, which is wired through these jacks before reaching the
toll switchboard. The test positions are provided with voltmeter, Wheatstone bridge,
test keys and cords, and trunks for testing lines and equipment and locating and
clearing troubles. The testboard jacks also serve to patch lines and equipment to spare
lines and equipment when the regular layout is in trouble or to make temporary circuit
changes.
POWER SYSTEMS 17-53
In step-by-step local or toll offices the testboard equipment is comparable to that provided
in manual offices except that the positions are equipped with rtmls and dialing trunks for
connecting to the various lines and equipments.
In panel died and crossbar local offices a local test desk test selector frame is employed,
consisting of a bay for sequence switches and a bay for relays, with terminal strips located
at the side of the frame. This frame is used to associate the local test desk with the final
selectors which are arranged for testing subscriber lines. The operation of the cutoff
relay in the subscriber line circuit may be controlled from a key in the test desk. The
six first selector circuits which connect to trunk circuits in the test desk have access to any
one of 15 second selectors, which terminate in final test selectors. Test trunk ringing
circuits are furnished as required. The test desk is equipped with voltmeter, test keys
and cords, trunks, Wheatstone bridge if desired, and other necessary apparatus for check-
ing the condition of and locating and clearing trouble on lines and equipment. In addition
to the test desk there are various frames for testing the operating condition of the equip-
ment, such as the outgoing trunk test frame, decoder test frame, and multiple registra-
tion test unit.
In crossbar toll offices a toll test board is provided for making overall tests on the toll
trunks in order to locate troubles and restore the trunks to normal. A jack field is pro-
vided through which the intertoll trunks are wired, and miscellaneous trunks are ter-
minated in this field. The circuits in this testboard are four-wire, requiring twin plugs.
For talking and monitoring, the circuits are reduced to two-wire by means of a hybrid
coil. A transmission-measuring system with the readings projected on screens at the
ends of the testboard, a noise-measuring unit, and a variable oscillator are provided as
part of the testing equipment. Outgoing toll trunks may be locked out (made busy) and
tested by dialing through the trouble tracing frame, which seizes the incoming trunk con-
nected to the outgoing trunk in trouble or to be tested and lights a lamp associated with
that trunk at the testboard. The desired outgoing trunk may also be seized by plugging
a test cord into the test jack appearance of the incoming intertoll trunk and operating the
lockout relay in the outgoing trunk through the connecting switches.
In addition to the toll testboard a maintenance center is provided for each No. 4 crossbar
toll system, in which various testing frames are located with a chief switchman's desk and
files in front of the frames.
The maintenance forces at this center are occupied with responding to alarms, making
tests, following up trouble reports and assistance requests, and maintaining records of the
operations.
7. POWER SYSTEMS
Power equipment for central offices is required to provide direct current for talking and
signaling and alternating and pulsating current for signaling and for many other aux-
iliary needs in telephone operations.
Power equipment for magneto offices usually consists of dry cells or a battery
eliminator to supply direct current to the operator's telephone set and a hand generator
and power-operated ringing device for ringing subscriber bells. Magneto subscriber
telephones are supplied transmitter current by dry cells at each telephone or other power
sources.
Power equipment consists of motor-generator sets and rectifier units (in common-battery
offices) for supplying direct current for the energization of subscriber telephone trans-
mitters, private branch exchanges or private automatic exchanges, central office cord and
operators' circuits, relays, switches, alarms, carrier systems, telephone repeaters, and
many other central-office units. Continuity of service is insured by the provision of
storage batteries which float across the d-c office power supply and, in case of commercial
power failure, will carry the office load for a short period of time, and by duplicate charging
units operated by other than commercial electric power.
The types of charging and load supplying power units (including storage batteries) and
of the signal supply units vary over a wide range of equipments, which have different
capacities, functions, and characteristics depending on the office power load demands and
the purposes for which the units are designed.
Att common-battery offices, both local and toll, require 24- and 48-volt d-c supply, which
may be provided by regulated rectifiers (mercury vapor, tungar, copper oxide, or selenium
types) for the smaller loads; and motor-generator sets, singly or in multiple units, for the
larger loads. In all cases, storage batteries of suitable capacity to provide for the 24- and
48-volt demand are bridged across the d-c power supply leads on a float basis; that is, the
office load is carried by the generating units, the batteries serving as an emergency source
of power. These offices may also require a 130-volt plate supply for carrier systems,
17-54
TELEPHONY
telephone repeaters, and other vacuum-tube devices, which supply may be furnished
from regulated rectifiers for small loads or from motor-generator sets for the larger loads.
Storage batteries of the proper capacity are also required across this supply on a float
basis for emergency reasons. Figure 49 shows a typical central-office power-plant ar-
rangement with a single floating battery and automatic control. Although only one
motor-generator set is shown, it is the usual practice to add these units for multiple opera-
tion as required.
Ringing and signal supply units may be of the vibrator or subcycle converter type for
small offices or motor-generator sets for the larger offices. These units are designed to
supply the usual 20-cycle, 75 to 175 volt ringing power, but certain multifrequency sets
EMERGENCY CELL
SWITCH
CONTROL
EMERGENCY^"!" J** .JZ,
CELLS
COUNTER
MOTOR-GENERATOR
SET
1 > I
III,
TO SECOND
MOTOR- GENERATOR
SET
FIG. 49. Typical Central Office Power Plant Arrangement with Single Floating Battery and Auto-
matic Control (Courtesy Bell System)
are also available for supplying harmonic frequencies of 16 2/3, 33 1/s, 50, 66 2/s, and, if
desired, 25 cycles, at from 75 to 175 volts, for selective party-line ringing. These units
also provide 110 to 120 volt d-c coin control supply, superimposed ringing with 46 to 52
volt silent interval tripping battery supply, howler tone (applied to lines with receivers
left off the hook), interrupter tones of various frequencies for operator and subscriber
signals, such as busy, trouble, or operating procedure.
In addition to the above types of signaling units there are several different types of
single and multifrequency generators producing frequencies for signaling, such as 135 and
1000 cycles, and for vacuum-tube oscillators.
All power equipment is automatically regulated to close limits.
RADIO TELEPHONE SYSTEMS
Radio telephone systems have been in operation for over 25 years, but with the growing
need for such systems in recent years, accelerated by World War II, they are rapidly
coming into use for many purposes in the communications field. Many of these systems
are arranged for connection to wire telephone plant, so that subscriber stations may be
interconnected over radio channels and wire line extensions to give local, national, and
world-wide service.
APPLICATIONS
17-55
8. APPLICATIONS
Radio telephone service is being employed today (1) between all of the larger and many
small countries, (2) within individual countries, (3) between ships at sea and fixed land
stations, (4) between coastal harbor and inland waterways ships and fixed land stations,
(5) between mobile vehicles of various classes and stationary points or other mobile units,
(6) between planes and ground stations or other flying planes, (7) directly between persons
(walkie-talkie), and (8) for special and emergency use, such as for fire, police, emergency
repair units, and for temporarily bridging gaps in telephone lines that have sustained
major damage.
Development work and trial tests are in progress for the use of radio channels (1) be-
tween and within trains and railroad operating control points, and (2) for rural line tele-
phone service. An important activity, now in the experimental stage, is the use of super
high-frequency (microwave) radio systems for toll telephone, television, facsimile, and
other services. Undoubtedly many other applications of value to the public will be found
for radio telephone systems.
Radio telephone systems may be listed at present under the following general classi-
fications:
1. Long-haul toll.
2. Short-haul toll.
3. Coastal harbor and
inland waterways.
4. Highway mobile.
5. Urban mobile.
6. Airways mobile.
7. Railway mobile.
8. Rural subscriber.
9. Special emergency.
Table 1 lists some of the principal operating data regarding these systems.
A new microwave radio relay system, using frequencies between about 2000 to 12,000 or
more megacycles, is installed between New York and Boston. This system, using "line-
sight" frequencies, requires seven intermediate relay stations, spaced on the average about
30 miles apart and located on relatively high elevations, as shown in Fig. 1. This trial of
/P1TTSFIELD
ASNEBUMSKIT MT.
1395'
/>/
II MILES. •
s& / ""
SPRIMGFJELD
.MASS.
CONN.
SQUARE BLDG.
(NEWENG-T.&T.CO.)
ELEV. *"*-'
JACKIE
JONES MT.
ELEV.1240y
FIG. 1. New York-Boston Radio Relay System (Courtesy Bell System)
microwave transmission is for the purpose of determining its efficiency, dependability,
and economy for multiplex telephony and for interconnecting sound broadcast and tele-
vision stations, and its application in the network of communications routes. The very
broad band of frequencies available for experimental use in the super high-frequency
(SHF) range, coupled with the fact that these waves tend to travel in a straight line and
are capable of being beamed by means of guiding lenses and reflectors, provides a promis-
ing field for experiments in communications, with the probability of eventually securing
17-56
TELEPHONY
•*£
Ji
1*3
3 S
i73
33
+20 to +30
+10 to +20
+20 to +30
+10 to +20
oo o
o 50,
a
i
o
ts
1
si:
53
£ =
5 .
Ss'3.1
0<NCNO
-
o o
CN O O
o' o" o"
5JQ^?5
i i i i
co oo
<S CM
I |
«M fS
1 I
CS <N
•S S
I ft
.^1
1 a
APPLICATIONS
17-57
Oto+35
0 fco +25
33
+ +
33
«A in.
+ +
52
1
+ +
+ +
+ +
+ +
0
-5 to +30
-5 to +20
-3
t
X
"o
8.
ns which aro n
0
to July 12, 194
' noise couditio
0
ii W
IS
u\ en
CM O
0 0
J> 4
0 0
tn —
r^ o
0*6
ai
O 0
0 0
0 0
0 O
o
0
0
Pablo for 25 Me and
higher value correat
X X
§ £
§ I
o
o
o
s
s
2 1
1 1
R C3
i FCC Pro
aes set nois
1 1
5 §
2
2
*
o
es
s f^
d to July 19,
The lower va
I
S
i
T
1
§
1
1111
-0
"" {Q ^ ?
o 30,000 Me, revise
i.
e dipole or whips,
To vehicle
From vehicle . . .
To vehicle
From vehicle . . .
To plane
From plane
To train
From train
To subscriber..
From subscriber
ill
Highway mobile
Urban mobile
Airways mobile
,
Railway mobile
Rural subscriber
Special
emergency
o£ I
17-58
TELEPHONY
large groups of telephone, telegraph, television, sound broadcast, and other useful chan-
nels.
The multicavity magnetron, a high-frequency power generator developed for radar,
has made possible 10,000-Mc frequency currents with peak powers ranging from 10 to
1000 kw for very short intervals of time.
The microwave radio relay system has been given a valuable tool in the lens-antenna,
consisting of an array of small metal plates mounted in a frame about 10-ft square. This
lens employs the same principle in focusing radio waves into a pencil beam as an optical
TRANSMITTER AND
SWITCHING CIRCUIT
CARRJER-
-=r OPERATED
RELAY
TO ADDITIONAL RECEIVER CIRCUITS
FIG. 2. Shore Circuit for Coastal Radio Service (Courtesy Bell System)
lens does in directing light waves. The radio waves are fed into this new lens-antenna
through a hollow-tube wave guide and horn at the rear, the waves spreading out along
the hornlike shields to the lens plates, which bend the waves and direct them out of the
front of the lens to produce an emergent wave front parallel to the front of the lens. This
type of antenna causes less wave distortion due to dimensional variations than would re-
sult from such variations in a parabolic reflector, and greater manufacturing tolerances
therefore are permissible. Also, the horn-type shield at the rear of the lens reduces rear-
ward radiation, present in reflector antennas, and the front of the lens may be protected
from weather by a plastic covering.
Multiplex operation over microwave radio channels was developed by the Bell Labora-
tories during World War II for use of the TJ. S. Army Signal Corps and proved to be of
great value to the armed forces. Its full possibilities for commercial service are being
explored. Army-type pulse modulated microwave systems are now in commercial service
between Los Angeles and Catalina Island as well as from the mainland to Nantucket Is-
land. As developed for war purposes, multiplex operation employed a highly directive
APPLICATIONS
17-59
and sharply focused microwave beam of about 5000 Me which carried eight separate mes-
sages. The intelligence of each channel is conveyed by varying the time position of the
1-microsecond channel pulses, eight of which (one for each channel) are transmitted in
sequence, 8000 times a second. Thus, if a 1000-cycle tone is being beamed over one chan-
nel, one cycle of this tone requires 1/iooo of a second, during which time eight pulses, spaced
at approximately equal intervals throughout the one cycle, would be transmitted. At
the receiving terminal these pulses are received in sequence by their respective channel
and, being representative of the electrical intelligence at the originating terminal, are re-
converted into sound intelligence. Two-
way operation is obtained by using a
separate radio channel in each direction
of transmission. Because of the method
of transmitting, this system has been
designated as pulse-position modulation
(PPM}.
Coastal harbor and inland waterways
radio telephone systems are extensive,
one consisting of 14 basic shore stations,
strategically located to cover the entire
coast from Maine to Florida, to Texas,
and up the Pacific coast to Seattle. Fig-
ure 2 shows a circuit of one of the shore
stations. Note that by use of the mon-
itor jacks the shore operator can select
the receiver giving the best reception.
Highway mobile radio telephone sys-
tems give the operator the same facility.
These systems consist principally of
(1) f-m (frequency modulation) radio
transmitters (about 50 to 100 miles
apart) and associated receivers at fixed
locations along the intercity highway which the system is to cover, (2) f-m radio trans-
mitters and receivers for the mobile units, and (3) a control terminal associated with each
fixed transmitter.
Wire lines connect the fixed receivers to the control tenninal, which provides for link-
ing the transmitter and as many as eight receivers to a two-way, two-wire line to the
central office handling the system.
In operation, a customer desiring connection with one of his mobile units moving along
a highway between his city and a distant point which is covered by a radio system asks
for the mobile service operator in his city. This operator has access over a wire circuit
to the various radio transmitters along the
highway and, on the basis of the probable
location of the desired mobile unit as fur-
nished by the customer, a code assigned
to the particular vehicle is dialed and is
transmitted by wire and by the selected
radio transmitter to the called vehicle.
This code activates a selector set in the
vehicle, which gives a visual and audible
alarm. In casing from the vehicle, the
occupant removes his handset from its
holder and presses his push-to-talk hand-
set button, which causes his transmitter
to send out a signal. This signal is re-
ceived by the nearest fixed receiver along
the route being traveled by the vehicle,
which converts the radio- to a voice-fre-
FIG. 3.
Mobile Radio Transmitter and Receiver in
Auto Trunk (Courtesy Bell System)
FIG. 4. Control Unit and Hand Set of a Mobile
Radio Unit Mounted under Auto Instrument Panel
(Courtesy Bell System)
quency signaL This signal then passes along the receiving wire circuit to the terminal
equipment at or near the telephone office and signals the mobile service operator.
Figure 3 shows a mobile installation of a transmitter and receiver in the trunk compart-
ment of an automobile; Fig. 4, a control unit and handset under the dashboard of an
automobile; and Fig. 5, a schematic of a two-tone selective signaling mobile unit.
Urban mobile radio telephone systems employ equipments like those in the highway
mobile service for transmitting and receiving telephone messages or signals. However,
since such systems are intended to cover only an individual city and its adjacent territory
17-60
TELEPHONY
(up to about 20 to 25 miles from the transmitter) , usually only one transmitting station
is provided at a central location in the city and a number of receiving stations are strate-
gically placed within the area to be served, so that the mobile transmitter signals will be
received and carried to the central office in the city, wherever the vehicle may be in the
area. One additional feature not provided in highway service is a one-way signaling serv-
ice: when certain signals are received by the occupant of the vehicle, certain action is to
be taken. Voice communication is not given in signaling service.
. The fixed f-m transmitter will generally have a power output of 250 watts using an as-
signed frequency in the 152-162 Me band. The mobile f-m transmitter will usually
have a 15-watt output at a different frequency in this band. Initially, mobile units will
be limited to one channel for a given city, and a number of such units will be assigned to
the same channel.
Selective signaling units, actuated by coded dial pulses transmitted from the fixed trans-
mitter and installed in the vehicles, will insure signaling only the vehicle being called. A
two-letter, five-digit code will be used, such as WU 2-5556, which will not be duplicated
OSCILLATORS
FIG. 5. Two-tone Selective Signaling System for Mobile Radio Service (Courtesy Bell System)
on the same frequencies, where interference might result. Since the mobile selector set
operates the calling signal on the twenty-third pulse, the sum of the digits (not including
letters) will always add up to 23, unless the plan of selection is later changed. Differ-
entiation between vehicles operating only in one local area and those that may operate in
more than one such area will be effected by assigning different code letters to the two
classes of vehicles.
Railway mobile radio telephone systems are now (1949) under trial tests by several
railroad companies (1) between trains and railway control points, (2) within the train
itself, and (3) for use of the passengers in talking to fixed telephones.
The last-mentioned service makes use of highway mobile installations, which in most
cases parallel the right-of-way. Service between passengers on moving trains and land
telephone systems may be rendered by carrier-induction methods, rather than by radio,
or by both types of transmission, as may seem best in the future.
Rural subscriber radio telephone systems are now in the trial stage, employing assigned
frequencies within the 152 to 162 Me band and low-power transmitters.
At Cheyenne Wells, Colo., a system has been installed (operating on a trial basis hi
the frequency range of 44 to 50 Me) which provides for rural radio service to eight ranches
located from 11 to 21 miles from the town. None of these ranches are reached by either
power or wire telephone lines, the operating power for the ranch radio sets being obtained
from home electric plants. Four of the ranches are served by direct radio links to the
Cheyenne Wells central office; the other four are reached by relatively short wire ex-
tensions from a nearby radio-equipped ranch. At the central office the eight stations
are grouped, through terminal equipment, to form an eight-party rural line.
Radio equipment at each of the first four ranches includes a transmitter, receiver, a
telephone set, and two antennas. The 10-watt transmitter and associated receiver are
housed in a steel cabinet, which can be located out of sight, with only the telephone in-
strument in view. The antennas are mounted on a pole or atop one of the ranch buildings.
At Cheyenne Wells, the equipment includes a 50-watt transmitter, receiver, and ter-
minal equipment for associating the various radio links with the central-office switchboard.
Further studies will be made, based on the results of the trial tests, to determine the
most practicable types of radio equipment to employ for rural service.
TRANSMISSION AND OPERATIONAL METHODS 17-61
Special emergency radio telephone systems have been in operation for many years to
serve fire, police, forestry, highway, utility companies, and a number of other services.
Operation is of low power output at frequencies generally within the 1.6-3.3 and the
30-40 Me bands.
The equipment employed for the mobile services is, in general, similar to the types dis-
cussed under coastal harbor, highway, and urban mobile service with variations required
for the particular type of service involved.
The telephone and other wire-using companies have been using for several years portable
emergency radio telephone equipment to bridge gaps in open-wire lines resulting from
sleet, flood, or wind damage.
One type of portable radio telephone system for emergency use employs a 50-watt
transmitter arranged to operate at one of ten selected frequencies within the 2,0-3.1 Me
band, and a receiver adjustable for any frequency within the 2.0-3.1 Me band. One
antenna at each terminal is switched between the transmitter and receiver, depending on
the direction of transmission, by a voice-operated control unit. A volume limiter in the
transmitter, and automatic volume control and a codan (carrier-operated device, anti-
noise) in the receiver, regulate the transmitter modulation and the receiver output and
operation to provide uniform transmission. Its operating range varies with the type of
terrain, noise, and atmospheric conditions from about 25 to 50 miles. Power for the
terminal units is obtained from 110-120 volt, 60-cycle supply. A sensitivity control
circuit actuates the transmitter at a minimum level of — 47 dbm (47 db below 1 milliwatt)
and likewise prevents line noise or room noise from causing false operation of the equip-
ment.
9. TRANSMISSION AND OPERATIONAL METHODS
Quiescent transmitter operation is employed either to save power or to permit the
installation of a single transmitter and receiver at the same location under conditions which
otherwise would prevent satisfactory communication. The transmitter is provided with
manual or voice-operated control means which render it sufficiently inactive during idle
intervals so that emission from it does not interfere with reception. If saving power is an
objective, the switching is directed toward securing nunimum power input during qui-
escent periods.
Two sidebands and carrier transmission is the most commonly used method, owing to
the simplicity of signal generation and detection. It requires a radio transmission band
equal to twice the highest audio frequency to be transmitted. The carrier contains no
intelligence-bearing signal component but simplifies detection and is useful for such con-
trol purposes as automatic tuning and volume control at the receiving end and for the
operation of auxiliary relays. The power required to transmit the carrier is large com-
pared with that required for the sidebands, and if the carrier is transmitted continuously
it represents a considerable loss. In the case of 100 per cent modulation by a single-
frequency tone, the carrier power is twice the sum of the power in the two sidebands.
Spread sidebands and carrier transmission uses sidebands displaced from their normal
positions in relation to the carrier by an amount approximately equal to the audio band
transmitted. It is sometimes used when inverter-type privacy is employed, because the
spreading then can be accomplished without additional modulating equipment and merely
requires that the inverter be designed for different input and output frequency bands.
Advantage: less stringent distortion requirements are imposed on radio equipment be-
cause predominant intermodulation products fall outside the used band. Disadvantage:
communication band, much wider than otherwise necessary, is occupied inefficiently.
Two sidebands, suppressed carrier, transmission has not been used, because the diffi-
culties of correctly maintaining the phase of the reintroduced carrier at the receiving end
generally offset the advantage of saving hi power capacity at the transmitter. Further-
more, suppression of one sideband as weU as the carrier usually offers additional advantages
with less stringent synchronization requirements, since in this case the frequency of the
reintroduced carrier can depart from the correct value by a few cycles without appreciable
mutilation of speech quality, and it can be off as much as 20 cycles without noticeably re-
ducing articulation.
Single sideband, suppressed carrier, transmission has certain important advantages
which are especially valuable in long-wave systems where transmitter power capacity,
communication band width, and static interference are controlling factors. These ad-
vantages, referred to double sideband and normal carrier modulated 100 per cent, are:
6-db increase in intelligence-bearing signal for same transmitter amplitude capacity,
3-db reduction in random received noise, no emission from transmitter during idle periods,
and radio transmission band no greater than audio band width. Disadvantages: more
17-62
TELEPHONY
complicated modulating process; precision frequency control is required in order to re-
introduce at the receiver the carrier suppressed at the transmitter; transmitter power
supply is subjected to large load variations at syllabic frequencies. This method is em-
ployed in the long-wave and short-wave systems between New York and London and on
some radiotelephone systems. In the short-wave system, synchronization of the re-
introduced carrier at the receiving end is accomplished satisfactorily by transmission of the
carrier or an equivalent pilot signal reduced 10 to 20 db below normal carrier.
Privacy is usually achieved by modifying the signals in one or more ways which render
the message substantially unintelligible unless received with special equipment. Devices
called speech inverters have been developed which reverse the sequence of the audio fre-
quencies before modulation in the radio transmitter; rein version is then necessary after
detection at the receiver. Additional privacy is obtained by varying the radio carrier in
a cyclic manner. A more complicated method, known as split-band privacy, involves
dividing the total audio band into several narrow bands. These can be inverted and/or
transposed in various arrangements, and the combination can be changed frequently.
All these methods have been applied successfully to radio circuits.
10. PRINCIPLES OF TWO-WAY OPERATION
SYSTEMS WITH FOUR- WIRE TERMINALS. Since the emission of radio waves
and their subsequent detection at a distant point constitute inherently a unilateral proc-
ess, duplex operation requires two one-way radio systems acting in opposite directions.
Such an arrangement for telephony is shown in Fig. 6. At each end of the system a
Radio Transmitte
Radio Receiver
Radio Receiver-^
dio Transmitter
FIG. 6. Simple Radio System — Four-wire Terminals
microphone is connected to a radio transmitter and a telephone receiver is connected to a
radio receiver. Thus, two persons can converse provided the radio transmission east-
ward does not interfere with the transmission westward; i.e., radiation from T2 reaching
RI must not prevent RI from functioning satisfactorily in receiving signals from TI. Like-
wise radiation from TI at RZ must not interfere with reception of signals from T%. For
the condition where the person at W is talking and the person at E is listening, the effect
of Tz at RI may be (a) increased noise, (6) distortion of signals from TI, (c) detection of
unwanted signals. Furthermore, the effect of TI at #2 may result in a return signal to
W which is quite disconcerting. If the person at W hears himself talking in reasonable
volume, it will not disturb him unless there is sufficient delay to give an echo effect. How-
ever, if he hears unintelligible sounds in like volume, they will seriously disturb him.
Such sounds appear if RZ is overloaded by high field intensities from TI or if TI produces
extra-band radiation within the selectivity band of RZ and of sufficient intensity to be
detected.
The forms of interference- outlined above are prevented by adapting one or a combina-
tion of the following expedients: (a) use of different frequency bands for the two direc-
tions of transmission, (6) geographical separation of the radio transmitter and receiver,
(c) use of directional antennas, (d) suppressing all emission from transmitters except during
transmission of wanted signal and disabling and protecting local receivers during active
intervals of adjacent transmitter. Accomplishing (d) involves switching operations.
Manual control of the switching is satisfactory for experienced talkers, but voice-current
control is favored for more general use. Single sideband, suppressed carrier systems are
less susceptible to interference than other systems and may be used more readily without
switching arrangements, if the transmitter and receiver are separated sufficiently.
PRINCIPLES OF TWO-WAY OPERATION 17-63
In planning a specific system, there is a wide variety of circumstances, including eco-
nomic factors and the characteristics of the particular apparatus to be used, which de-
termine the selection of the method or combination adopted. There are no clearly de-
fined dividing lines, but it may be stated rather generally that the use of (a} or (d) alone is
satisfactory for short-distance working. All long-distance systems employ at least (a)
and (6) or (6) and (d). Geographical separations range from a few hundred feet to sev-
eral hundred miles. _ Use of (c) reduces the distance necessary. With (a) the necessary
geographical separation is determined by the attenuation required to bring the ratio of
field intensities of the wanted and unwanted signals within the limits of the receiver se-
lectivity and overload characteristics. With (<2), geographical separation is necessary
for high-power transmitters, to avoid exposing the receiving system to noise due to spu-
rious emanations from parts of the transmitting apparatus or the associated power-supply
system.
SYSTEMS INTERCONNECTING WITH TWO-WIRE EXTENSIONS. Since stand-
ard telephone subscriber loops are two-wire circuits in which messages in opposite direc-
tions traverse the same wire path, the two oppositely directed radio paths in Fig. 6 must
be arranged to terminate two-wire. The ordinary hybrid coil arrangement common in
telephone repeaters and four-wire cable circuits fails to solve this problem except where
the radio circuit meets all the requirements imposed by wire practice on corresponding
wire circuits. This is seldom possible or economical on account of difficulties peculiar to
the radio paths. In wire systems, transmission levels remain fixed within closely es-
tablished limits, and signal volumes vary over a considerable range. In radio circuits,
comparatively large variations in attenuation sometimes occur in relatively short intervals
of time, except over extremely short-distance paths, and these tend to cause retransmission
of received signals at such amplitudes that severe echoes and even singing around the two
ends of the circuit will occur unless means are provided to prevent it. Furthermore, for
all long-distance working, it is uneconomical to provide transmitter capacity which will
permit appreciable variations in signal volume. To obtain maTin-mm signal-noise ratios
at the radio receivers, it is essential that the speech currents fully load the transmitters.
This requires gain adjustments between the hybrid coils and the transmitters to suit the
particular talkers and the condition in the connecting wire circuits.
To overcome these fundamental transmission difficulties, automatic switching systems
operated by the voice currents of the speakers have been developed. These devices block
the radio path in one direction while speech is traveling in the reverse direction and also
keep one direction blocked when no speech is being transmitted. The operation is so
rapid that it is unnoticed by the telephone users. Since these systems prevent the exist-
ence of singing and echo paths, then- use permits the amplification to be varied at several
points almost without regard to changes in other parts of the system, and it is possible
by manual or automatic adjustment to maintain the volumes passing into the radio link
at relatively constant values irrespective of the lengths of the connected wire circuits and
the talking habits of the subscribers.
Figure 7 is a schematic diagram of one end of a circuit showing the essential features of
a voice-operated device. This kind of apparatus is capable of taking many forms and is,
of course, subject to change as improvements are developed. The diagram illustrates how
one of these forms might be set up. This form employs electromechanical relays. The
functioning of the apparatus illustrated is briefly as follows: the relay TES contact is
normally open so that received signals pass through to the subscriber. The relay SS con-
tact is normally closed to short-circuit the transmitting line. When the subscriber at
W speaks, his voice currents go into both the transmitting detector and the transmitting
delay circuits. The transmitting detector is a device that amplifies and rectifies the voice
currents to produce currents suitable for operating the relays TES and SS, which there-
upon short-circuit the receiving line and clear the short circuit from the transmitting line,
respectively. The delay circuit is an artificial line through which the voice currents re-
quire a few hundredths of a second to pass so that when they emerge the path ahead of
them has been cleared by the relay SS. When the subscriber at W has ceased speaking,
the relays drop back to normal. The function of the receiving delay circuit, the receiving
detector, and the relay RES is to protect the transmitting detector and relays against op-
eration by echoes of received speech currents. Such echoes arise at irregularities in the
two-wire portion of the connection and are reflected back to the input of the transmitting
detector, where they are blocked by the relay RES which has closed and which hangs on
for a brief interval to allow for echoes that may be considerably delayed. The gain con-
trol potentiometers, shown just preceding the transmitting and receiving amplifiers, are
provided for the purpose of adjusting the amplification applied to outgoing and incoming
signals.
The relief from severe requirements on stability of radio transmission and from varying
17-64
TELEPHONY
speech load on the radio transmitters, which such a system provides, permits much greater
freedom, in the design of the two radio circuits than would otherwise be possible. In the
system shown in Fig. 7' interference between local transmitter and receiver, as outlined
previously in discussing Fig. 6, is prevented by such geographical separation as may be
necessary in combination with either the use of two communication bands or single side-
band, suppressed carrier, transmission. When one communication band is used for both
directions with carrier and double sideband transmission, the switching systems of the
type shown in Fig. 7 are extended to operate additional devices which suppress the car-
rier at the transmitter and disable the receiver. This switching is necessary to protect
Vprom Distant
I Transmitter
Subscriber Tefephone
Operator
FIG. 7. Two- wire Radio Terminal Showing Arrangement of Voice-operated Switching Devices
the receiver where it is exposed to intense fields from the transmitter. When privacy ap-
paratus is included in an installation, the voice-frequency switching is frequently arranged
to transfer the same privacy unit from the transmitting to the receiving leg of the four-
wire terminal (or vice versa) , thus saving cost of a second privacy unit.
11. SYSTEM DESIGN
The designer of a radio circuit is limited to the establishment of certain facilities at the
transmitting and receiving station which are expected to yield the desired results on the
basis of available data, computations, and previous similar experience. Beyond this
point, the performance is inherently a matter of probability, since transmission is subject
to the vagaries of natural influences entirely beyond the control of man. Sometimes,
very short-distance circuits can be provided which are substantially immune from these
influences. However, the designers of long-distance circuits frequently encounter tech-
nical limitations which determine the maximum degree of reliability attainable, quite
apart from considerations of cost.
The design proceeds from a statement, which includes (a) type and nature of service
expected, (6) daily hours of operation, (c) general location of terminals, (d) distance cov-
ered and character of intervening region, (e) overall transmission requirements, (/) future
plans. From these now the requirements and compromises which ultimately determine
the selection of transmission frequencies and methods; the location and general arrange-
ment of transmitting, receiving, and voice terminal stations; and the choice of equip-
ment.
Systems requiring separate transmitting and receiving stations usually involve expend-
itures which warrant a fairly comprehensive preliminary survey. The survey includes a
search for suitable station sites and measurements of received field intensities, noise levels,
and angles of wave arrival over the approximate path at substantially the proposed fre-
quencies. This survey frequently can be effected by observing the signals from existing
telephone or telegraph stations. It serves to substantiate conclusions derived from
computations and from available transmission data; it gives important specific information
concerning noise at receiving sites; and it should serve to disclose any conditions peculiar
to particular locations which may have a profound effect upon performance.
SYSTEM DESIGN 17-65
TRANSMISSION REQUIREMENTS are related intimately with the needs and objec-
tives of individual applications to such an extent that the statements herein should not
be taken as concrete recommendations but should be regarded principally as guides to the
items that need consideration when formulating the specific requirements for a particular
system.
Circuits terminating four-wire and used only for direct conversations between terminals
can be operated over a wide scale of conditions all of which may be acceptable for the
purpose in hand. Circuits interconnecting with telephone plants should conform as far
as possible to the standards of the wire systems in respect to transmission, stability, dis-
tortion, and interference effects. Allowance must be made for similar imperfect con-
ditions in wire transmission. Otherwise the complete connection may be unsatisfactory,
even though it is possible to converse over the radio circuit alone. With the possible
exception of very short-distance radio circuits, it is generally true that radio transmission
conditions vary through an extremely wide range, and it becomes necessary during some
operating intervals to endure a comparatively poor circuit or temporarily do without one.
It is desirable, therefore, to make the limiting requirements as liberal as possible.
Transmission Times. The requirements are no different from those for corresponding
wire systems. The transmission time, from radio transmitter input terminals to receiver
output terminals, is seldom appreciably greater than the time required for radio waves
to traverse from transmitter to receiver. The propagation rate is approximately 186,000
miles per second. To this must be added time for wire circuits to the control centers,
time for delay networks used with voice-operated switching devices, and time for any
delays incurred in other apparatus, such as privacy systems.
Stability. It is desirable that all equipment adjustments that affect the overall circuit
performance, and more particularly those that cannot be made without removing the cir-
cuit from service, retain the established conditions for long periods.
Receiving-set selectivity, in addition to discriminating sharply against unwanted sig-
nals, should provide ample margins for the total effect of frequency drifts to be tolerated
over a period of several hours at all points in the system where base frequencies are gen-
erated. For example: a system employing a quartz-plate oscillator at the transmitter
and a well-designed beating oscillator of the tuned circuit type at the receiver, when
operating at 15 Me and transmitting audio frequencies up to 3000 cycles, requires an
intermediate-frequency band width of the order of 8000 cycles (— 3 db at 4000 cycles from
midband) .
When the system is operated on the basis of constant net loss, it is desirable that the
loss in the radio circuits be held to ±1 db. When the system is operated on the basis of
constant input volume to the radio transmitter and voice-operated devices are used, vari-
ations of d=5 db are sometimes tolerated at the receiving end. When radio transmission
is subject to rapid variations the receivers are provided with automatic volume controls
which hold the output volume within a few decibels for wide fluctuations in the signal-
field intensity.
Audio distortion is usually specified in terms of transmission band characteristics,
amplitude or load characteristics, and departure from proportionality of phase shift with
frequency. Difficulties from the last are seldom encountered in ordinary radio circuits
used for voice communication.
Transmission Band Characteristics. The requirements in each instance axe closely
related to the needs of the particular application. Except when using radio frequencies
less than 100 kc, it is seldom a difficult matter to provide reasonable bands for conversa-
tional purposes. The minimum requirements for international radio telephone circuits,
as recommended by the International Consultative Committee on Telephony, are the
same as for long-distance wire circuits: i.e., 300-2600 cycles as the limiting frequencies
effectively transmitted. The committee also recommends that future circuits be designed
to transmit at least 200—3000 cycles. Widening the band improves quality and to a lesser
extent improves articulation, provided that other conditions do not become controlling.
For instance, exposure to random noise at the radio receivers is substantially proportional
to the band width, so that widening the band may not result in improved performance
under adverse receiving conditions. In the United States, it is customary to specify the
transmission-frequency characteristic in terms of departure in decibels from the trans-
mission level at 1000 cycles.
Amplitude or Load Characteristics. Except when radio circuits are subject to rapidly
varying transmission conditions, such as those frequently encountered in the short-wave
range, load tests are made in the same manner as for wire circuits, and the requirements
are the same for equivalent results.
The linearity requirements for the transmitting system and the receiving system are
usually specified in terms of distortion products resulting from the application of pure
17-66 TELEPHONY
tones. The tests are made separately for the two systems. Carrier and double sideband
systems may be tested with a single tone at varying amplitudes. Single sideband sys-
tems require two-tone tests. If privacy apparatus is to be used with double sideband
systems, it is usually required that the total distortion products introduced by the trans-
mitter alone or the receiver alone and falling within the audio band shall be about 25 or
30 db below the single tone output for any tone input up to 90 per cent modulation. If
two equal tones are used on any system, it is generally specified that any distortion product
falling within the transmission band shall be 20 to 25 db below one tone. (For testing
methods, see Section 11 and I.R.E. Report of Standardization Committee.)
Radio-frequency or phase modulation at the transmitters results in troublesome distor-
tion effects at the receiving station if radio transmission occurs simultaneously over two
or more paths differing in length by appreciable portions of the wavelength used. This
situation is encountered in the short-wave systems, and it is sometimes specified that,
during the modulation cycle, the phase shift associated with frequency modulation or
phase modulation should not exceed ±15°. (For method of test, see I.R.E. Report of
Standardization Committee.)
When no appreciable differences in simultaneous transmission path lengths are en-
countered, frequency modulation can be tolerated if all the radio equipment has sub-
stantially a flat frequency-transmission characteristic throughout a band sufficiently wide
to pass all the essential frequencies generated and if extra-band radiation does not inter-
fere with other services.
Interference is caused by signals from other radio circuits and by disturbances generally
classified as noise.
Unwanted signals may enter the radio circuit through cross-modulation effects at the
transmitting station if there are two or more transmitters, or they may enter at the re-
ceiver. Cross-modulation is likely to occur with open-wire transmission lines. It is not
difficult to overcome if active lines are well separated and long parallel runs are avoided.
It results from the impression on the tube circuits of one transmitter of modulated radio-
frequency voltages generated by a second transmitter coupled to the first usually via the
transmission lines or the antennas. In special cases, trap circuits or other simple filtering
devices are introduced when found necessary, but they are objectionable if the same lines
are to be used for several frequency assignments.
At the receiving station it is not enough to provide apparatus having comparatively high
selective properties. It is necessary to know in what manner this selectivity is achieved,
and what values of unwanted signal voltage may be impressed upon the receiver input-
terminals simultaneously with the wanted signal. A receiving site and an antenna sys-
tem must then be selected which will not violate these receiver requirements.
Noise at the receiving terminal is derived from the connecting wire system, the radio
transmitting and receiving apparatus, and the radio noise field. If noise from the wire
system meets the accepted standards for good toll circuits, as it should, it is not likely to
have a noticeable effect on the performance of the* radio circuit. Noise generated within
the radio transmitter is measured in terms of audio signal by means of a linear monitoring
rectifier exposed to the transmitter radio output. The audio signal-noise ratio thus ob-
tained should be somewhat better than the maximum audio signal-noise ratio which it is
desired to obtain at the receiving end under conditions of high signal-field and low noise-
field intensities. Noise due to the receiving equipment should never be a controlling
factor except when approaching the limit of sensitivity.
Since the effect of noise depends greatly on its frequencies in relation to the audio trans-
mission band, precautions are necessary in systems employing frequency inversions to
prevent the conversion of relatively harmless noise into very objectionable noise. This
conversion may occur if the noise enters any part of the system between points where the
inversions and reinversions are made.
The interfering effect of noise is very difficult to express accurately.
12. INSTALLATIONS
The successful establishment and maintenance of dependable, long-distance circuits
with two-wire terminations require careful installation planning, the provision of adequate
testing facilities, and the consideration of many problems only indirectly related to the
technical operation of the system. There is a wide gap between this extreme and the
simple facilities required for short-distance radio circuits without two-wire extensions
(Section 7).
TRANSMITTERS AND RECEIVERS AT SAME LOCATION. Small transmitting
systems for short-distance service are placed at the same location as the receiving sys-
INSTALLATIONS 17-67
terns. The transmitter and receiver are usually self-contained units requiring a single
connection to the general power supply. If the same frequency assignment is used for
both directions of transmission a single antenna is sufficient. Manual or voice-controlled
switching is necessary to change from receive to transmit conditions. If two frequency
assignments are used without quiescent transmitter operation, it is frequently found more
satisfactory to employ two antennas slightly separated than to make provision for trans-
mission and reception on the same antenna. The latter is possible by means of various
special circuit arrangements but is almost certain to incur a penalty in respect to min-
imum receivable field intensities. Since the field intensity gradient around the trans-
mitting antenna is extremely steep, it is seldom necessary to remove the receiving antenna
more than 50 to 500 ft in order to secure satisfactory conditions. The distance depends on
transmitter power, type of antenna, frequency difference, receiver selectivity, and load
characteristics. If the antennas have directional properties, the relative positions should
be selected, when possible, so that each antenna presents a null in the direction of the
other. Usually the transmitting antenna is erected near the apparatus, and the receiving
antenna is placed at a distance from the receiver, connections being provided by suitable
transmission lines.
If it is essential that the transmitting and receiving apparatus be installed in close
proximity, attention needs to be given to shielding to prevent direct interference between
transmitter and receiver. Receivers designed for this type of installation seldom require
further shielding when used with transmitters up to about 25-watt capacity, provided that
the transmitters are also reasonably well shielded. It is a good plan to place receivers
somewhat away from transmitters for ratings up to about 500 watts. The alternative is
to provide a special shielded compartment for the receiver. This has been done on ship-
board, where space limitation and operating convenience demand a compact installation.
As the transmitter power is increased, the possibilities increase rapidly that noise will
enter the receiver directly or through the receiving antenna from various sources within
the transmitter or its power circuits. If this occurs, it limits the permissible receiver
sensitivity and may completely nullify the value of higher power for the purpose of work-
ing greater distances. Recourse to voice-controlled quiescent transmitter operation
greatly alleviates this type of interference for installations where two or more transmitters
are not to be used simultaneously. It is frequently applied to ship systems and ma-
terially increases the working distances. It is effective only hi eliminating noises related
to the suppressed radio signal components. Around large transmitters the residual noise
after the carrier or other radio signal components are suppressed still prevents the use of
extremely sensitive receivers. This is one of the compelling reasons for establishing
separate transmitting and receiving stations for long-distance circuits, where extremes of
power and sensitivity are essential.
SELECTION OF TRANSMITTING STATION SITE. Items requiring consideration
are: ground conductivity and dielectric constant; general character of surrounding ter-
rain; position relative to receiving stations; possibilities of interfering with broadcast re-
ception or that of other services; transportation, power, and telephone facilities; living
arrangements for station personnel; prevalence of sleet storms; unusual conditions of tem-
perature, humidity, presence of salt spray; etc. Ground conditions affect antenna design.
Desirable characteristics depend upon the type of radiating system to be employed, the
frequencies and the wave angles of transmission (Sections 6 and 10). The terrain in the
direction of transmission affects the vertical wave angle. Mountains and bills subtending
large angles are undesirable. Steel towers, buildings, transmission lines, etc., constituting
sizable obstructions directly in front of short-wave directional antennas, are objectionable
since they modify the directive pattern.
THE TRANSMITTING STATION LAYOUT is based primarily on the requirements of
the antennas and their relation to the transmitter. Usually the antenna or antennas are
located a short distance away from the building housing the transmitter, and connection
is made through open-wire or concentric transmission lines. The practice of bringing
the antenna downlead directly to the transmitter is seldom followed in modern installa-
tions. Use of uniform transmission lines, all having the same impedance, greatly simplifies
switching problems. Good values are: open-wire 600 ohms, concentric lines 70 to 80
ohms. Placing the antennas clear of the transmitter building avoids difficulties in erec-
tion and maintenance. Short-wave directional antennas are placed so that the building
is not within the horizontal angle of the principal lobe.
RECEIVING STATION EQUIPMENT depends somewhat on the number of radio
circuits involved but is also influenced considerably by the standards established in re-
spect to service interruptions other than those attributable to the transmitting medium.
The essential components are: radio receiver and its power-supply units, antennas and
transmission lines, wire-terminal apparatus and voice-frequency testing equipment with
17-68 TELEPHONY
associated power-supply units, general power supply, including emergency power sources.
Large stations usually have facilities for observing the field intensities of received signals
and noise and for the precise measurement of received frequencies. These are used to
cheek the transmitters which are a part of the system, and those of other systems, which
create interference.
SELECTION OF RECEIVING STATION SITE is a matter demanding careful con-
sideration, especially if long-distance services are contemplated, and it is seldom safe to
make a final decision without actual observations of signal-field and noise-field intensities
over a period sufficient to obtain representative data. Items that should receive attention
are: location relative to transmitting stations of same system and all other nearby trans-
mitters and sources of man-made noise; local ground conditions and general character of
surrounding terrain in the direction of wave arrival; transportation, power, and telephone
facilities; living arrangements for station personnel; prevalence of electrical storms; un-
usual conditions of temperature, humidity, presence of salt spray, etc.
It is desirable to have the antennas present nulls toward all transmitters in the area
which are likely to produce any form of interference.
Likely sources of man-made interference are: high-tension transmission lines, electrical
machinery in factories, electrical trains, automobiles, airplanes, motorboats, etc. The
last three mentioned are particularly important in long-distance short-wave reception at
times when signal-field intensities are low as the result of magnetic disturbances. With
an extremely sensitive receiver and a directional antenna designed for low-angle reception,
no serious interference would be expected from automobiles 1 1/2 miles in front of antenna
and 1/2 to !/4 mile at the sides and rear.
Reception of short waves arriving at low angles can frequently be improved from 5 to
10 db by placing properly designed antennas on ground sloping uniformly downward in
the direction of the transmitting station at an angle of 5° to 15°.
RECEIVING STATION LAYOUT. Primary objectives are to place the antennas in
an advantageous position for the collection of energy from the incoming waves and to
obtain an efficient arrangement in respect to transmission lines. In choosing directional
antenna locations, close attention should be given to the position of objects capable of
reflecting or otherwise redirecting unwanted waves into the sensitive angles of the antenna
characteristic.
It is well to adopt a uniform impedance for all transmission lines. Convenient values
are: open wire 600 ohms, concentric lines 70 to 80 ohms. In order to avoid disturbing
the incoming radio waves, and also to avoid undesirable currents, transmission lines
should be placed as near the ground as practicable. However, it is inadvisable to place
two-wire lines less than 6 ft from the ground. Pour-wire balanced lines are disturbed less
by the proximity of the ground and have been used successfully at 4-ft elevations. Con-
centric lines may be installed underground. They should always be sealed and, in some
situations, are further protected from moisture by maintenance of pressure with inert gas.
Aside from somewhat higher first cost, much can be said in favor of concentric conductors,
since they substantially eliminate the difficulties encountered with converging lines at re-
ceiving set locations. At short-wave stations, it is desirable to have all directional an-
tennas present a null to the building and the road approaching it.
SHIP STATIONS are usually installed in extremely limited quarters. They require
compact units, designed to allow inspection and repairs without having access to all sides
and preferably without disconnection and removal of parts. Rapid frequency-changing
features are especially important if it is desired to maintain close contact with more than,
one shore station,
Transmittuig and receiving antennas are usually separated as much as possible. Simple
types are generally used because they are suitable for several frequencies. Horizontal
directional properties are not desirable. Electrical noise conditions vary widely with
positions aboard ship.
A four-wire termination is usually employed to avoid rather expensive control-office
equipment. Ship's passengers talk from a conveniently located booth. Circuits are also
provided from the captain's quarters or a similar point convenient to the bridge. With a
four-wire terminal, no voice-operated switching apparatus is needed other than the simple
devices necessary for quiescent transmitter operation. Voice-frequency apparatus is
mounted adjacent to the receiver. One attendant supervises all operations and performs
the duties of a technical operator. If the ship is equipped with radio telegraph as well
as telephone apparatus, and the two must operate simultaneously, precautions are neces-
sary to avoid mutual interference.
SHORE STATIONS are usually equipped to offset, as far as practicable, unfavorable
conditions aboard ship. This is done by providing transmitter power capacity from 10
to 40 times that of the ship station, by employing directional antennas, and by selecting
SERVICE REQUIREMENTS — TOLL 17-69
a quiet receiving location a few miles away from the transmitting station. Antennas
having moderately directional patterns (6 to 12 db maximum net gain) are used to cover
the principal ship lanes effectively. Less directional antennas are needed for general
coverage. When a ship is close in, at "which time the required direction of transmission is
likely to move rapidly through a wide horizontal angle, antenna gain is less important, and
a directional antenna, unless it has pronounced nulls, is frequently found satisfactory be-
cause the unfavorable ship position is offset by the short distance. Otherwise, a simple
antenna is provided for this purpose.
BIBLIOGRAPHY
Articles in Proc. I.R.E; Elec. Rev. (London) ; Elec. Communication; Bett Syst. Tech. J.; Trans. AJ.I5.E.;
Elect. Engg.; Proc. I.E.E. (EngL); Electrician; Wireless World; Bett Lab. Rec.; Rev. gen.
Ann. des -pastes.
TELEPHONE LINES— TRANSMISSION
CONSIDERATIONS
13. TYPES OF PLANT
SUBSCRIBER LINES (LOOPS) include all types of outside plant facilities needed to
connect the subscriber station telephones with their local central office. Such facilities
may consist of cable, either aerial or underground, open (bare) wire, carrier or radio chan-
nels, or a combination thereof. Generally, cable is used in urban areas as a means of
serving local subscriber stations; where small urban open-wire plants are still in operation
they are rapidly being replaced. In rural areas, open-wire lines are still in general use
except in congested sections, since the fewer lines and longer distances characteristic of
rural areas make the open wire more economical. As stated above, however, it is an-
ticipated that radio facilities can be made available, commercially, to serve distant or rel-
atively inaccessible farms where the costs of providing the usual telephone wire facilities would
be excessive.
TOLL LINES, as generally defined, consist of various types of outside plant facilities
employed to provide toll circuits between toll centers (TC). Those line facilities connect-
ing TC and tributary offices are considered part of the TC plant. These latter offices, in
the general meaning of the word "tributary," are small offices (in territory adjacent to the
TC) connected to the TC by one or more tributary circuits and are fully or partly depend-
ent upon the TC for the handling of their toll traffic. Toll facilities may consist of cable,
aerial or underground, open wire, carrier or radio channels, or a combination of these.
Subscriber line facilities, known generally as exchange plant, and toll line facilities should
be designed and constructed to meet, cooperatively, the overall service objectives which
are known collectively as service standards. These standards are not fixed for all time but
change with service needs and advancements in the art of communications.
TRANSMISSION AND SIGNALING are two fundamental factors to consider in any
telephone system, whether the connecting facilities between subscribers are wire, carrier,
radio, or a combination of two or more of these types. If either transmission or signaling,
or both, are not satisfactory for a given telephone system, the system is not workable
under modern standards of service.
14. SERVICE KEQUIEEMENTS— TOLL
UNIVERSAL SERVICE is the goal toward which the telephone industry has been
striving for many years and which, it now appears, will be attained. This goal simply
means that anyone, anywhere, can talk, telephonically, with anyone else, anywhere else,
whether the connection be established locally, within the nation, or between any two coun-
tries in the world. For a number of years it has been possible to talk by telephone from
any point in the United States to any other point connected to the nationwide toll system
and to many foreign countries. Worldwide service is being rapidly expanded to include
those countries not at present reached.
TRANSMISSION OF SPEECH between two points requires that speech (sound)
power from the talker actuate his transmitter diaphragm and that the transmitter con-
vert this power into electrical power, which travels to the distant listener's receiver, where
17-70
TELEPHONY
it is reconverted by the receiver diaphragm into speech (sound) power of approximately
the same characteristics as the original speech power. It is obvious that the electrical
power will diminish as it travels over the circuit between the talker and listener stations
as the result of series and shunt impedances encountered in the lines and equipment which
constitute the circuit. If the electrical power reaching the receiver is diminished to the
point where it no longer drives the receiver diaphragm sufficiently to permit the listener's
ear to interpret the intelligence carried by the resulting sound waves, then the electrical
transmission loss in the circuit is too high to permit carrying on a satisfactory telephone
conversation. It, therefore, becomes necessary to limit overall transmission losses and
consequently the losses in component parts of circuits, which usually consist of two or
more sections or links.
THE GENERAL TOLL SWITCHING PLAN (Fig. 1) as developed for establishing toll
connections on a manual basis provides a practicable plan for accomplishing universal
"SEE
NOTE1
[+3]
JO
1
g
TC
FOR CIRCUITS DESIGNED TO HANDLE ONLY TERMINAL BUSINESS THE WORKING NET LOSS
DEPENDS UPON TOLL TERMINAL LOSSES INVOLVED AND UPON OVERALL DIRECT STANDARDS.
AS A TYPICAL EXAMPLE, WITH A DIRECT STANDARD OF 18 DECIBELS, THE LIMITING VALUES
OF TERMINAL CIRCUIT NET LOSSES WOULD BE AS SHOWN BELOW FOR THE ASSUMED VAL-
UES OF TOLL TERMINAL LOSS.
PO 1Q Pp
PO
13 TC
TC 16
TC
NOTES:
1. THE TOLL TERMINAL LOSS WOULD BE DETERMINED IN EACH CASE ON THE BASIS OF MEETING THE
TRANSMISSION REQUIREMENTS IN THE MOST ECONOMICAL AND SATISFACTORY MANNER, FOR EX-
AMPLE, IN MEETING THE 10 DECIBEL UMJT FOR OUTLET TERMINAL LOSS. THE VALUES SHOWN
ABOVE ARE TYHCAL BUT THE ECONOMICAL TOLL TERMINAL LOSS IS EXPECTED TO VARY CONSID-
ERABLY IN INDIVIDUAL CASES.
2. PAD VALUES DEPEND ON NOISE AND CROSSTALK CONDITIONS, ON LIMITING TOLL TERMINAL LOS-
SES AND ALSO, IN THE CASE OF INTERMEDIATE LINKS, ON ECHO MARGIN REQUIREMENTS.
STANDARDS
2 -LINK THRU PO-
2 -LINK THRU TC
3 -LINK •
4 -LINK
5 - LINK 23
OUTLET TERMINAL LOSS — 10
TC
CODE
TERMINATING TOLL
CENTER
PO PRIMARY OUTLET
RC REGIONAL CENTER
•VvV SWITCHING PAD
INDICATES TYPICAL
TOLL TERMINAL LOSS
(6) MINIMUM WORKING
ECHO NET LOSS (AS-
SUMES NO TRANSMIS-
SION IMPAIRMENTS)
9 EFFECTIVE WORKING
NET LOSS -VIA CONDITION
[+3] ECHO MARGIN
FIG. 1. Typical Example of the General Toll Switching Plan, Showing Limiting Toll Circuit Losses
_ (Courtesy Bell System)
service in the United States and throughout the world, with the development and ex-
pansion of telephone systems in other countries.
From Table 1 it will be noted that any two subscriber telephones which have access to
the nationwide toll network can be connected together, using not more than five toll cir-
cuit links and four switches. It is assumed that the telephones are located at their re-
spective toll center (TC) points, i.e., not at tributary points, which would necessitate
using a tributary trunk to reach the respective TC office.
The plan provides for eight regional centers (RC}, Atlanta, Chicago, Dallas, Denver,
Los Angeles, New York, San Francisco, and St. Louis, each being strategically located
within the United States, to serve as toll switching centers of the first order. Each of these
centers is connected by direct, high-grade toll circuits to each of the other centers. Within
each RC area are a number of important toll centers known as primary outlets (PO), each
SERVICE REQUIREMENTS — TOLL
17-71
being connected by direct, high-grade toll circuits to its own RC, other RCs and other
POs, as required to best handle the traffic. Finally, each PO serves directly all the toll
centers (TC} within its area, and the TCs serve the subscribers within their local areas,
either directly or through their tributary offices. Thus, the plan provides for a con-
centration of the toll traffic at the various toll centers which have access to or are ac-
cessible from any part of
the nationwide system Table 1. Overall Standards
(including Bell and Inde-
pendent) through direct
or switched connections.
Table 1 shows overall
standards and number of
links ' and switches, and
Table 2 shows assigned
losses for the different toll
links, under the present
general toll switching
plan. * The letter codes are defined in Fig. 1.
In general, four-wire
circuits (a separate path for each direction of transmission) or carrier channels are em-
ployed for the long-haul, intermediate toll links because of their better performance at
low losses than that of two-wire circuits. Two-wire circuits are generally used for the
shorter end links and toll trunks.
Table 2. Allowable Toll Link (Circuit) Losses
ToH Connection *
(for switched traffic)
Overall
Standard,
decibels
Number of
Circuit
Links
Number of
of
Switches
Direct .
17-20
1
0
TC-TOTC
22
2
I
TC-PO-PO-TC
21
3
2
TOPO-RC-TC
21
3
2
TC-PO-RC-RC-TC
22
4
3
TC-PO-RC-RC-PO-TC
23
5
4
Toll Link
(for switched traffic)
Effective
Working
Net Loss,
decibels
Minimum Working Echo
Net Loss, decibels
(assumes no transmission
impairments)
Echo
Margin,
decibels
TC-PO (end link)
IO-(TTL) *
7-(TTL)
-r3
PO-PO (intermediate link)
1
3
-2
PO-RC (intermediate link)
RC-RC (intermediate link)
PO terminal loss
I
1
lot
3
3
-2
-2
* This value depends upon the most economical and practicable toll terminal loss for each individual
toll center which will meet the required primary outlet (PO} terminal loss of 10 db.
t This value results from taking one-half of the loss (20 db) for a tw>4ink connection through a
gain center (PO or RC).
The PO terminal loss of 10 db is fixed, unless changed under the plan. This loss may be
allocated to the TC-PO circuit and the toll terminal loss as required. Toll terminal losses
(TTL) vary from about 0 to 5 db.
TOLL CIRCUIT OPERATING REQUIREMENTS. The minimum working net loss
(MWNL} of a toll circuit is the lowest net loss that may be assigned that will satisfy the
design objectives imposed by singing, echo, crosstalk, and noise, when subject to maximum
negative transmission variations.
Tlie minimum working echo net loss (MWENL) is the lowest 1000-cycle net loss which
can be assigned so that a circuit will satisfy the echo objectives, including the assigned
echo margin. If the loss at which a circuit is operated is greater than the loss required
to offset the echoes arising from the circulating current paths within the circuit, a positive
echo margin is said to result. If the reverse is the case, a negative margin will be intro-
duced. In order to operate the plant at lowest over-all losses on built-up or switched
connections consisting of two or more TvnVs, positive echo margins have been assigned to
some classes of circuits and negative margins have been assigned to others. Switching
arrangements are so designed that negative margins will be offset in any connection.
Echoes are the result of imperfect balances in toll circuits equipped with telephone
repeaters and four-wire terminating sets. The two-wire circuits are necessarily converted
to four-wire circuits at each repeater, and the four-wire circuits require four-wire terminat-
ing sets at their terminals to convert the four-wire circuit to two-wire before extending
it to the toll switchboard. At certain important switching offices, four-wire switching
on a mechanical basis may be applied. At the points of conversion, a balancing network
terminates one branch of the hybrid coil, and the opposite branch of this coil is connected
to the outgoing or incoming toll circuit or the extension to the switchboard. It is not
practicable to match the impedance of the toll circuit exactly or the extension with the
17-72
TELEPHONY
impedance of the network. Thus, part of the voice currents are transferred across the
hybrid bridge into the repeater inputs in varying degrees at each repeater or terminating
set on the circuit instead of dividing equally between the outgoing line and its balancing
network. These currents which enter the repeater inputs will be amplified and travel
back to the talker with some delay, so that he hears his own words (in reduced volume)
coming back to him an instant after he has
spoken them. The listener may also be af-
fected. As the delay and return volume in-
crease, the annoyance becomes greater and
may reach the point at which the conversation
is not satisfactory. Figure 2 shows minimum
working net losses for terminal grade circuits
as limited by echoes, versus typical lengths of
toll cable without echo suppressors and with
anti-sidetone sets.
To overcome echo difficulties, repeater gains
must be properly assigned and regulated. Also,
an echo suppressor has been developed which,
by voice current action, causes a high loss to
be introduced in one side of the four-wire cir-
cuit while speech is being transmitted on the
other side. A simple schematic of this device
is shown in Fig. 3. Generally, two-wire cir-
cuits are relatively short and do not require
f
1/7
v/
EVEN HYBRID
EVEN
TRANSMISSION
PATH
o too 200 300 4oo soo eoo 700 echo suppression.
DISTANCE IN MILES The minimum working singing net loss
FIG. 2. Minimum Working Net Loss of Ter- (M"WSNL) is the lowest net loss assignable to
minal Grade Circuits as Limited by Echoes, a circuit which will meet singing requirements
^ut^lf sSLSS? £F™2«h"/£t£ ** indicated above under "echoes," the unl
sidetone Sets (Courtesy Bell System) balances existing in practice at the hybrid coils
of telephone repeaters and four-wire terminat-
ing sets cause part of the outgoing energy from one branch of the four-wire circuit to
pass through the hybrid coil bridge points to the opposite transmitting branch of the
four-wire circuit. At each hybrid coil this action occurs, so that, whether the circuit
consists of only a two-wire repeater with terminating lines or a long four-wire circuit with
several intermediate repeaters and a four-wire terminating set at each end of the circuit,
a circulating current is established, provided that the net circuit gains exceed the net
circuit losses in the circulating current
circuit and the phase change in the cir- ''OWV
culating current is a multiple of 360°.
It is thus necessary in designing cir-
cuits, particularly two-wire, to limit
these circulating currents by assigning
repeater gains, so that, for an average
circuit net loss, the most critical two-
wire repeater for 95 per cent of the
connections will have losses which total
at least 10 db more than the gains in
the two directions of transmission. For
the short terminal circuits with one or
two repeaters, an 8-db singing margin
will usually be satisfactory.
Figure 4 shows minimum working
net losses, as limited by singing, versus
typical toll cable circuit lengths for
specified conditions of repeater spacing
and singing points.
Tne TniTtiTntiTn working crosstalk net
loss (MWXNL) is the lowest net loss
assignable to a circuit which will satisfy
p— i — nsw^ —
•=• L— W\
EVEN RELAY
FIG. 3. Schematic of Echo Suppressor Circuit (Cour-
tesy Bell System)
crosstalk requirements under all operating conditions. Crosstalk is the electric and mag-
netic transfer of speech or similar currents from one telephone message circuit to another.
It may or may not be intelligible, but when it is composed of confused noise from several
sources it is known as babble.
Crosstalk usually results from cumulative, slight unbalances between circuits or high
SERVICE REQUIREMENTS — TOLL
17-73
energy level differences acting through close couplings in cable or open wire. The trans-
ferred energy is amplified wherever telephone repeaters are present.
Two types^ of crosstalk, near end and far end, develop between circuits. The first type
travels to a listener on one circuit in a direction opposite to the transmission from a talker
on another circuit; the latter type travels to the listener on one circuit in the same direction
as the transmission from a
talker on another circuit.
Near-end crosstalk occurs in
wire but not in properly ar-
ranged carrier circuits (ex-
cept W.E. Co. G-type) ; far-
end crosstalk appears in both
wire and carrier circuits.
The effect of crosstalk on
subscriber conversations de-
pends not only on the actual
volume of crosstalk heard
but also on circuit and room
noise present, circuit losses,
and personal reactions.
Crosstalk is controlled pri-
marily by avoiding excessive
energy level differences and
couplings ^ between adjacent
parallel circuits. Techniques
have been developed to limit
both level differences (by
3
100 200 300 400
500
Miles
600 700 800 900 1000
FIG. 4. Minimum Working Net Loss as Limited by fc
Typical Toll Cable Circuit Lengths (Courtesy
; versus
tern)
proper regulation of repeaters and other amplifiers) and high couplings and to employ
different frequency bands in controlling crosstalk.
Figure 5^ shows minimum working net losses, as limited by crosstalk, versus typical toft
cable circuit lengths.
Crosstalk values have generally been expressed in terms of crosstalk units, which are
defined as^one million ^lO6) times the ratio of the crosstalk current or voltage at the ob-
serving point on the disturbed circuit to the current or voltage at the sending point on the
disturbing circuit (assuming equal impedances at these two points). If the impedances
are not equal, the square root of the power ratio may be used in place of the current or volt-
age ratio. With the development of visual indicating apparatus for measuring crosstalk
and noise, crosstalk measurements have more generally been made in terms of crosstalk
coupling loss-db^ which means the net transmission loss between the sending point on the
disturbing circuit and the receiving point on the disturbed circuit, it being understood that
the higher the measuring set reading (loss),
the less the actual coupling. More recently,
the term db above reference coupling-dbx has
come into use. This term means the cou-
pling in decibels above reference coupling,
and reference coupling means the coupling
which would be required to give a reading
of 0 dba on a W.E. Co. 2B noise-measuring
set connected to the disturbed circuit when a
test tone of 90 dba (using the same weighting
as on the disturbed circuit) is impressed on
the disturbing circuit.
The 2B set is designed to measure cross-
talk and noise volumes or couplings (as well
as other quantities) in decibel values. These
~T4 values can be adjusted to a. common basis
for different types of lines and telephone
FIG 5. Minimum Working Net Loss as Limited receivers so that a given adjusted value, des-
by <**«* C—'ignated dba, will mean the same interfering
effect to the ear, regardless of the type of
8000T
6000
5000
^4000
= 3000
s-
^2000
1
^ 1000
i
i
i
H4
4-2
5(
t W
re)
—
y
^
a 800
£ 600
0 500
400
300
200
100
HF
•^
;
^
s
H4
4-2
5(2
> W
re)
A
/
/
\\
/
/
/
I
4
38J
-5C
an
i H
88-
50
2 4 6 8 10 12
Minimum Working Net Loss (Decibels)
line or subscriber set, affected by the crosstalk or noise being measured.
Figure 6 shows the relation between* the terms crosstalk units (cu), crosstalk coupling
loss, db, and crosstalk coupling, dbx.
The present design requirements for crosstalk limitations in circuits are taking into
account the wide reactions of different people to different amounts of crosstalk, the vari-
17-74
TELEPHONY
ation in crosstalk volumes due to the variation in speech power of different talkers, the
action of room and line noise on crosstalk effects, the intelligibility of crosstalk, costs in-
volved in its control, and attainment of a good balance in judging the importance of the
various factors entering into circuit design.
CROSSTALK COUPLING LOSS IN DECIBELS Present practices indicate that it is inadvisable
too 90 so 70 60 50 _40 to perniit crosstalk couplings in excess of 30
dbx (equivalent to 60 db crosstalk coupling loss
or to 1000 crosstalk units), as measured from
the transmitting to the receiving switchboard
for a single disturber circuit.
Noise transmission impairments which may
exist in toll circuits due to power line induc-
tion, noise generated within telephone systems,
or circuit irregularities must be limited to
avoid transmission penalties in circuit opera-
tion. Noise reaching the subscriber's ear
through his telephone receiver is, in fact,
equivalent to adding loss to the circuit. Table
3 shows how these penalties are evaluated in
terms of noise levels-dba.
Reference noise (RN) is used as a base in
the calculation of circuit noise in terms of dec-
ibel penalties, as given in Table 3. Reference
noise is registered as 0 dba on a 2B noise-
measuring set when the input into this set is
10 ~12 watt of 1000-cycle power (line weight-
ing). UN is equivalent, when measured at
the terminals of a 600-ohm line (with line
weighting), to 7 noise units; if measured across
the terminals of a W.E. Co. No. 144 receiver,
IO,OOO
8,000
6,000
4.OOO
2,000
3 1,000
. 800
^ 600
3 400
}
•> 100
80
fin
/
/
/
/
f
/
/
/
/
/
/
/
/
40
/
20
/
10
/
-10 o TO 20 30 40 so it is equivalent to 14 noise units.
CROSSTALK COUPLING , DBX Circuit noise of 29 db above RN (200 noise
FIG. 6. Chart showing Relation between Cross- units) Or less in a 600-ohm line is not con-
talk Units, cu; Crosstalk Coupling Loss in sidered to offer any appreciable noise impair-
Decibels; and Decibels above Reference ^ j j.- i ± * \. ± i
Coupling, dbx (Courtesy BeE System) ment to a conversation, but for about each
3-db increase in noise level above 29 db the
impairment increases 1 db, which must be included in the overall circuit loss.
Remedial measures have been perfected for controlling most types of noise to avoid
penalties.
Distortion transmission impairment (DTI) to conversations results from a restricted or
modified transmission of the full voice-frequency band necessary for clear, understandable
speech. Such restriction or modifica-
tion may be due to a low cutoff fre-
quency of certain types of loaded line
facilities and line apparatus. The older
H172-63 loaded cable facilities and cer-
tain early types of telephone repeaters,
carrier systems, and filters give distor-
tion impairments. The latest types of
loaded cable facilities, such as H44-25
and H and B88-50, and the latest-type
standard repeater and carrier systems
are considered to offer no appreciable
distortion for the usual lengths em-
ployed. Figure 7 and Table 4 show
distortion impairments for different
facilities with FIA-AST subscriber sets
and H88 switching trunks, as used in
the Bell System.
Volume transmission losses in toll
circuits will vary with changes in tem-
perature and, in addition, for open-wire
IN DECIBELS
\
EFFECTIVE CUTOFF FREQUENCY IS
THAT FREQUENCY AT WHICH THE
OVERALL NET LOSS OF THE TOLL
CIRCUIT IS 1O DECIBELS GREATER
THAN THAT AT 1000 CYCLES,
\
\
\
N
X
s^
\
**^
•^^
*****
L8 2.0 2.2 2.4 2.6 2.8 3.0 3.2 3.4 3.6
0 EFFECTIVE CUTOFF FREQUENCY OF TOLL CIRCUIT
IN KILOCYCLES PER SECOND
FIG. 7. Diagram Showing Distortion Transmission
Impairment for Different Facilities with FIA-AST
Subscriber Set and H-88 Switching Trunk, versus Ef-
fective Cutoff Frequency of Toll Circuit (Courtesy Bell
System)
facilities with such conditions as rain, sleet, and snow. These transmission variations
are different for aerial and underground cable and open wire and also change with fre-
quency.
SERVICE REQUIREMENTS — TOLL
17-75
Table 3. Noise Transmission Impairments Corresponding to Uoise Magnitudes Measured
or Computed at Various Points in the Transmission Circuit
Type of circuit <
Toll circuits
Toll connecting,
tandem and in-
teroffice trunks
Local loops
Point of i
estima1
neasurement or J
e . 1
Receiving toll
switchboards
Local office
Subset
terminals
of loop
Across receiver
terminals
I
Impedan
device
ce of Measuring f
1
600 ohms, termi-
nating, 6000 ohms
bridging *
600 ohms, termi-
nating, 6000 ohms
bridging *
600 ohms
terminating
Approximately
2000 ohms
Noise
Rating
Noise
Transmission
Impairment,
decibels
Noise Magnitudes in dba
Line Weighting
Line Weighting
Line
Weighting
Receiver
Weighting
NO
Nl
N2
N3
N4
N5
N6
N7
0
1
2
3
4
5
6
7
0 -29
29.1-32
32. 1-35
35.1-38
38. 1-40
40.1-42
42. 1-43
Over 43
0 -26
26. -29
29. -32
32. -35
35. -37
37. -39
39. -40
Over 40
0 -20
20. -23
23. -26
26. -29
29. -31
31. -33
33. -34
Over 34
0-17
17. -20
20. -23
23. -26
26. -28
28. -30
30. -31
Over 31
* When bridging measurements are made on a line, 600-ohm impedance is assumed each way from
the bridging point. Under these conditions (a) with 144 rec- line weighting, a correction f of +11 db
is added to 2B set readings and (6) with FIA line weighting, a correction f of about -f 18 db is added
to 2B set readings, in order to express readings in dba. If impedances each way from bridging point
are not 600 ohms, correct 2B set readings as follows:
Each impedance 300 ohms, correction is +3 db.
Each impedance 400 ohms, correction is +1-8 db.
Each impedance 900 ohms, correction is — 1.8 db.
Each impedance 1200 ohms, correction is —3.0 db.
Each impedance 2000 ohms, correction is —5.2 db.
t The corrections thus indicated should be added before entering Table 3.
Present Bell System practices provide for maintaining toll circuits of minimum to max-
imum lengths within the following deviations from the specified value: voice-frequency
(VF) cable, ±1.0 to ±4.0 db; K-carrier, ±2.0 db; VF open wire, ±1.0 to ±3.0 db;
open-wire carrier, ±2.0 db; and various combinations and lengths of facilities, ±1.0 to
±4.5 db.
Such limitation is provided for long VF cable circuits by devices known as automatic
transmission regulators spaced at proper intervals along the circuit to automatically acid
or reduce gain in the circuit as required to maintain the specified volume limits. Figure
8 shows a pilot wire transmission regulator circuit, with its pilot wire cable pair in the same
cable as the regulated cable circuits. Long cable circuits have a regulating repeater (in
place of the regular repeater) about every 150 miles. These repeaters are oontroEed at
each point by a master regulator, in accordance with temperature change in the pilot wire,
which causes the repeater gains to vary above or below normal setting in steps varying
from 1/4 to 1 db over a range varying from 2.75 to 19 db as required to maintain normal
level. No system of automatic regulation has seemed necessary for use with open-wire
voice-frequency facilities.
Since in cable circuits the attenuation-frequency curve is appreciably different at dif-
ferent temperatures, it is necessary to correct for this difference, known as twist, for high-
frequency carrier systems, such as the K-system. The twist effect in a 100-mile aerial
toll cable is shown in Fig. 9. Twist correcting circuits, as shown in Fig. 10, are located
in long cable circuits about every 100 miles for aerial and 200 miles for underground cable.
For open-wire carrier systems, pilot channel regulator equipment is incorporated in
the carrier terminal and repeater design to maintain transmission levels.
The effective transmission: loss of a toll circuit is equal to the 1000-cyde loss plus any
noise or distortion transmission impairments, all expressed in decibels.
The overall effective equivalent of a complete toll connection from subscriber to sub-
scriber is the sum of the effective transmission loss of the toll circuit or circuits and the toU
terminal losses at the terminating toll centers.
17-76
TELEPHONY
Table 4. Distortion Impairments
Voice Frequency
Facility
2-Wire
or
4-Wire
Filter
(Note 4)
Length in Miles for Various Impairments
-1 db
Odb
-Hdb
4-2 db
+3db
+4db
+5db
+6db
H245-S
2-W
2-W
No repeater
A
0-10
10-40
0-7
40-70
7-30
70-100
30-50
H155-P
2-W
2-W
No repeater
A
0-20
20-60
0-10
60-100
10-40
40-50
H174-S,H172-S
2-W
2-W
4-W
4-W
No repeater
B
B
A
0-35
0-15
35-70
15-50
70-100
50-90
0-300
90-160
160-270
Over 300
m E106-P
2-W
2-W
4-W
4-W
No repeater
B
B
A
0-60.
0-25
60-110
25-60
60-150
0-300
150-220
220-300
Over 300
H63-P
2-W
2-W
4-W
4-W
No repeater
C
C
B
Any
0-300
0-75
300-700
75-180
Over 700
180-450
BorE8S-50,SorP
2-W
2-W
2-W
4-W
4-W
No repeater
D
C
D
C
Any
0-150
0-200
150-450
0-100
Any
100-250
250-400
Over 400
H44-25, S or P
2-W
2-W
2-W
4-W
4-W
No repeater
D
C
D
C
Any
0-150
0-800
150-450
0-1000
0-100
Over
1000
100-320
Over 320
N.L. open-wire side
with 3KC carrier
line filters
2-W
2-W
2-W
No repeater
1059B
C
Any
0-800
0-300
Over 800
Over 300
N.L. open-wire
phan. or sides
with 5 kc or no
carrier line filters
2-W
2-W
2-W
2-W
No repeater
D
1059B
C
Any
Any
0-800
0-300
Over 800
Over 300
Type of Carrier Frequency Circuit
Maximum Number of Links for Various Impairments
-Idb
Odb
-Hdb
+2db
+3db
+4db
+9db
C2, C3, C4— Manual regula
tion
1
2
5
C2, C3 — Automatic regulati
on
1
2
4
Over 4
C4— Automatic reg
ulation .
2
5
C5
Any
D
1
2
EB
Any
GI . ...
2
HI — No repeaters
1
3
J
Any
K
Any
L
Any
Notes:
1. Impairments are referred to a distortionless toll circuit containing a 250-3000 cycle band-pass filter having square-
cutoffs.
2. Impairments are substantially independent of gage.
3. Impairments are substantially independent of type of line repeater, provided standard equalization is employed..
4. A refers to 13A or 32 A filters; B, to 13B.32B or 128B filters; C, to 13C, 32C or 12SC filters; D, to D93985, 32C
modified per KS-4165 (D 160523), or 128 A filters. 1059B filter is associated with the high level 22-type repeater
(104-D tubes).
SERVICE REQUIREMENTS — TOLL
17-77
REGULATOR SECTION
c
SHORT SECTION
1
PILOT WIRE CABLE PAIR LONG
SECTION
/
1 ^
.1-
n r
1
GALVANOMETER
MECHANISM
TO NO.2
REGULATOR
!
V
XJx
LJ
MASTER
RELAYS
W-E
_J
>
<
r
>
,
CABLE
FIG. 8.
------------- REGULATOR OFFICE ------------- *
Pilot Wire Transmission Regulator Circuit (Courtesy BeD System)
The desired overall transmission loss having been apportioned to the various compo-
nent parts of toll connections, as shown under the plan, the pattern for the engineering of
toll facilities is thus fixed. The toll ter-
minal loss as determined for each toll
center is defined as the average (one-half
of the sum) of the effective transmitting
and receiving losses (see article 15) from
the toll circuit termination to (and in-
cluding the efficiency of) the subscriber
station apparatus. With this loss deter-
mined for a given toll center, the toll
switching trunks and subscriber loops
(exchange plant) must be engineered to
meet this requirement, although ex-
change plant engineering also is subject
to exchange standards.
TOLL CIRCUIT LINE-UP PRO-
CEDURE consists of adjusting the op-
erating gains of voice frequency and carrier repeaters, carrier system terminals, and other
associated apparatus, such as switching pads, equalizers, attenuators, and other devices
necessary for proper operation of the toll circuits.
£? DEVIATION PROM 55* F NET LOSS
Q IN OECIBEUS
' ^LOSS GAIN-*.,
• ,.*>. w 0 w *
\
\
^
TEMP. (N
Jr\
3SGRS
no .
55
ES F
,-~~
/
^
— •-,
*-— ..
-^
•—-
-^
/
5 IS202S3O354O455055W
FREQUENCY 9* KILOCYCLES PER SECOND
Twist Effect in 100-mile Aerial Cable Circxi
(Courtesy Bell System)
17-78
TELEPHONY
INTERSTAGE NETWORK
FIG. 10. Twist Correcting Circuit for Type K Carrier System (Courtesy Bell System)
From the general toll switching plan (Fig. 1) it is evident that intermediate toll circuits
cannot be used for terminal traffic with the very low losses assigned without having ex-
cessive echo, singing, crosstalk, and other troubles. It is thus necessary to provide
switching loss pads in each of these circuits at each end and in the end link circuits (PO-TC)
at the primary outlet end, which pads remain in these circuits for terminal traffic and are
automatically switched out of the circuits for via (through) traffic. The total pad loss
usually employed is thus equal to the difference between the operating net loss of a given
circuit in its terminal and via conditions.
In general, when a circuit meets the design objectives in the via condition and the loss
of the switching pad or pads satisfies the crosstalk objectives in the terminal condition,
singing will also be satisfactory; also, echo will be within limits if the pad loss is at least
equal to the assigned negative echo margin.
Transmission levels on toll circuits require careful coordination with other adjacent
or nearby circuits to prevent excessive crosstalk. Also levels should be relatively high
(within the capabilities of the associated equipment) to provide suitable signal-to-noise
ratios. Levels of about -f-3 to +6 db generally are employed at the input to two- wire
lines, and from +4 to +10 db at the input to four- wire voice-frequency lines. Open-wire
carrier system units employ about +16 db (input to the line) for Bell-owned systems.
TOLL LINE SIGNALING usually employs 2CK 135-, or 1000-cycle signaling systems.
For short non-composited toll facilities, 20-cycle signaling is usual; for the longer toll
circuits having composite sets 135- or 1000-cycle signaling is required. Since 1000-cycle
signaling will readily pass along any type of message circuit that will transmit voice fre-
quencies as such or in modulated form, this type of signaling is general for all long toll
circuits. For crossbar toll operation, as described in article 3 of this section, pairs of fre-
quencies in the range of 700 to 1700 cycles are sent out over toll trunks for pulsing the de-
sired signals.
15. SERVICE REQUIREMENTS— EXCHANGE
EXCHANGE PLANT STANDARDS are based largely upon giving the telephone-using
public a convenient, satisfactory service at the least cost consistent with protecting the
investment and employee interests.
The establishing of exchange plant standards involves taking into consideration the
•efficiency of subscriber telephone sets as well as loop, trunk and central-office equipment
(COE) losses and signaling ranges. It is thus necessary to establish a means of rating
subscriber loops and trunks with respect to a known transmission standard in order that
the capabilities and costs of the various types of equipment and line facilities that are
available for use in exchange plant may be compared and it may be judged whether or
in what respect the equipment facilities meet the assigned standards for a given exchange.
Overall transmission standards are the upper limits for the overall effective station-to-
station transmission and form the basis of plant design. In the practical application of
such standards, allowances are usually deducted for room noise, and sometimes for other
impairments, from the overall standard so that the resulting design standard may be used
directly in the design of the exchange plant.
SERVICE REQUIREMENTS — EXCHANGE
17-79
The determination of the most desirable transmission standards for a given exchange is
a matter of engineering and business judgment, based on a comprehensive view of local
conditions and on past performance.
On the basis of general usage of the W.E. Co. FIA-AST or equivalent subscriber sets,
Bell System practices contemplate ultimately overall exchange transmission standards
of 10 to 14 db for multiomce exchange area traffic, with the possibility of the standards
being 1 or 2 db higher for tandem operation. In single-office areas the standard is gen-
erally taken as approximately equal to the loop limit, considering both transmission and
signaling.
A working reference system was devised some years ago by the Bell System as a means
of rating exchange loop and trunk plant. This system* shown in Fig. 11, includes two
identical common-battery subscriber loops, each connected through a 24-volt battery-
feed repeating coil, to a variable, distortionless (up to 3000 cycles) 600-ohm impedance
SUBSCRIBER
SET
NO. 337
TRANSMITTER
NO. 144
RECEIVER
NO. 46 COIL
STANDARD
CONNECTION
3 Ml. 22 GA.
(0.082 MF
PER MILE)
REPEATING VARIABLE REPEATING
COIL TRUNK COIL
LOOP
SUBSCRIBER
SET
600W
3000^
CUT-OFF
—
NO. 337
3MI.22GA.
(0.082 MF-
PER MILE)
TRANSMITTER
NO. 144
RECEIVER
NO. 45 COIL
STANDARD
—
CONNECTION
C) AS AN ALLOWANCE
FOR RELAY, OFFICE WIRING AND HEAT COILS
LINE NOISE = 100 NU IN RECEIVER
"TYPICAL" ROOM NOISE
FIG. 11. Working Reference System for Specification of Effective Losses (Courtesy Bell System)
trunk. The length of loops and types of station and central-office apparatus are typical
of conditions and apparatus existing at the time the system was devised and are still re-
garded as suitable for reference purposes.
The working reference system is so designed that it permits comparing effective trans-
mission losses, which include volume and distortion losses, line and room noise, and side-
tone effects. The system itself has an actual effective transmission loss or rating of 18 db,
based on 7.5 db in the transmitting loop, 1.8 db in the receiving loop, and 8.7 db in the
trunk. The line and room noises included in each loop are respectively 100 noise units
(NU) and room noise comparable to that in quiet offices or fairly noisy residences. This
room noise is equivalent to 50 db RAP (reference acoustic power, which is 10 "^ watt of
sound power per square centimeter at the listening ear) .
EFFECTIVE TRANSMISSION PERFORMANCE of exchange telephone plant, as
interpreted in the United States and some other countries, is evaluated by the generally
accepted method of counting the number of requests to repeat words or sentences, in a
short interval of time, made by talkers with average volume over the circuit to be eval-
uated. Other methods of evaluation, such as the "immediate appreciation" method,
have been studied but have not been adopted in the United States.
For convenience, each effective loss is considered to have three components — volume,
distortion, and sidetone losses. The distortion and sidetone losses in the working ref-
erence system are considered to be zero for reference purposes, and the effective loss of this
system is thus numerically equal to the volume loss.
The individual effective losses which make up the effective loss of a complete circuit
are:
1. Transmitting loop loss.
2. Receiving loop loss.
3. Trunk loss.
4. Terminal junction loss.
5. Central-office loss.
6. Intermediate junction loss.
7. Loss due to line noise.
The effective loss due to room noise is not considered a circuit loss, although it does affect
conversations.
Losses 1 and 2 are determined by comparing the effect on conversation of the element
or complete loop to be rated with the effect of the corresponding element or complete loop
of the reference system, using the other components of the reference system to complete
17-80 TELEPHONY
the talking circuit. Thus, since the effective loss of the transmitting loop of the refer-
ence system is 7.5 db, any transmitting loop which is substituted for the reference loop and
which gives the same grade of service (repetition rate) also has an effective loss of 7.5 db.
However, if the substituted loop gives the same grade of service after an increase of 2 db
is made in the variable reference trunk loss, then the substituted loop has an effective loss
2 db lower than the reference loop, or if the reference trunk loss is adjusted to 2 db less than
normal the substituted loop has an effective loss 2 db higher than the reference loop.
Receiving loops are rated in the same manner, using the reference receiving loss of 1.8 db.
A given trunk may be rated by substituting it for the reference trunk and using the
reference loops in the connection. The adjustment in the reference trunk loss deter-
mines the rating of the given trunk (called the effective connecting circuit loss) with respect
to the reference trunk loss of 8.7 db, the fact that the assigned effective loss of the refer-
ence trunk is equal to its attenuation below 3000 cycles being kept in mind. The ef-
fective connecting circuit loss thus obtained is not in a useful form but may be made so by
dividing it into an effective trunk loss and two effective terminal junction losses (one at each
end) , which latter are considered equal for this symmetrical circuit.
This division between trunk and junction losses is necessary for the practical establish-
ment of a set of effective trunk loss curves, since for each type of trunk the terminal junc-
tion losses are different for each different combination of loops, sets, and central offices at
the trunk terminals. The effective trunk loss consists of the volume attenuation of the
trunk and that part of the distortion that is proportional to trunk length, thus permitting
the establishing, for each type of trunk, of a value of effective trunk loss on a per mile
basis. Each effective terminal junction loss includes a volume reflection correction plus one-
half of that part of the distortion loss of the trunk that is not included in the effective trunk
loss plus a correction for the effect on sidetone of the trunk impedance. The effective
terminal junction losses can thus be considered as correcting factors which, when added to
the sum of the other losses, will give the correct effective loss for a complete circuit.
The assumption that the effective connecting circuit loss (trunk rating) is made up of a
constant plus a loss proportional to length is a good approximation for complete circuits
containing a single type of trunk, except for effective trunk losses of about 5 db or less
and for coil loaded trunks of any effective loss. For the low-loss trunks, accuracy in de-
termining the trunk loss is not usually important. For loaded trunks, the curve of con-
necting circuit loss versus length departs from a straight line, because the end sections
change with a change in the trunk length. However, if the connecting circuit loss is
plotted only for lengths permitting half-section termination, a smooth curve is obtained
which closely approximates a straight line above 5-db loss, and this curve may be used
to determine the trunk loss per mile and the terminal junction loss for this termination.
Similar curves, approximating straight lines, paralleling the one for half-section termina-
tion, may be set up for any other desired end section at each end. Such approximate
straight lines determine the effective terminal junction losses for the respective end sec-
tions chosen. Thus, the effective connecting circuit loss of a loaded trunk, terminated at
half-section at one end and at other than half-section at the other end, is considered as
made up of the effective trunk loss per mile times the total geographical length of the trunk
in miles (including the end sections) plus the effective terminal junction loss for each end
section.
The effective loop losses apply directly only with the 600-ohm reference trunk. The
effective trunk loss applies satisfactorily for any combination of loop, set, and central
office, but the effective terminal junction losses obtained with the reference loops do not
apply for other combinations of loop, set, and central office. The terminal junction losses
for other combinations of these elements, including other than the reference trunk, may
be determined as required.
EFFECTIVE LOOP LOSSES include the loss of three different types of simplified
central-office circuits, namely, the 24-volt repeating coil circuit used in the working refer-
ence system, a 48-volt repeating coil circuit typical of standard circuits for toll connections,
and a 48-volt step-by-step circuit used in local dial offices.
In practice, actual central-office circuits have equipment and wiring, additional to the
simplified circuits, the loss of which is dependent upon the actual loop and trunk condi-
tions. However, a single value of loss for the additional equipment and wiring for each
type of office and connection is usually sufficient if it is determined under typical limiting
loop conditions. The effective local offices losses are therefore determined between the
working reference loops and trunk for the more commonly used central-office connecting
circuits.
For trunks composed of different types of facilities, such as 19- and 22-gage cable,
intermediate junction losses occur at each junction of the dissimilar types of facilities be-
cause of reflections of energy at these points. Such losses have been determined for var-
SERVICE REQUIREMENTS — EXCHANGE
17-81
ious combinations of facilities used in the Bell System and must be added as part of the
overall trunk loss.
Effective losses due to line noise (Table 3 of this section) should be added to the other
effective losses in a given loop when the electrical noise at the receiver terminals of the
loop is greater than the reference noise (100 units) assumed in the reference loops. Less
noise than reference noise in the receiver is considered equivalent to reference noise.
In addition to the above-mentioned losses, if the room noise for a given loop is more or
less than the room noise (50 db RAP) assumed for the reference loop, effective room noise
losses corresponding to the difference between the actual and assumed room noise must
also be added to the overall given loop loss. Figure 12 shows the effective loss due to
room noise versus room noise of different intensities for two different sidetone conditions.
Il
ihg
Sg I
il §
3 15
-5
A
7
A
f
S.HIGH SIDETONE,
NO. 46 INDUCTION CO!
STANDARD CONNEC-
TION
-/
w
m
/
M
^A, LOW SIDETONE,
ANT1-SIDETONE
INDUCTION COILS
A
7
/
f
/
>*
f
^^
<^
$
$?
>>^
-20 -15 -10 -5 O 5 10 15 20 25 3O
ROOM NOISE IN DECIBELS ABOVE TYPICAL VALUE
35
FIG. 12. Effective Receiving Loss Due to Room Noise, versus Room Noise of Different Intensities
(Courtesy Bell System)
The values shown are approximate, since it is difficult to determine the actual losses due
to room noise because of a number of variable factors, some of an intangible nature.
The Bell Telephone Laboratories have made field and laboratory investigations com-
paring the ease of carrying on a telephone conversation over different circuits in actual
service, and also studying the physical characteristics of circuits and instruments, as well
as their ability to transmit speech sounds, using syllabic articulation tests under a large
number of variable conditions encountered in service. From these investigations a
number of effective transmission loss curves showing effective loop losses in decibel versus
loop length in thousands of feet have been prepared for the commonly used types of cen-
tral offices, loop facilities (cable or open wire) , and telephone sets, based on the working
reference system.
Figure 13 shows separate effective transmitting and receiving loss curves (provisional)
for both 24-volt exchange grade and 48-volt toll grade battery supply and also the average
(T + R)/2 curves for both grades of battery supply. These particular curves apply for
W.E. Co. type 1 or 10 Manual or Panel Dial Offices, non-loaded 22-BSA gage cable loops,
and the latest-type W.E. Co. Antisidetone (AST) subscriber sets with FIA (handset) or
635-706A (deskstand) type instruments. These curves are typical of other sets of sub-
17-82
TELEPHONY
scriber loop loss curves for different types of central offices, loop facilities, and sets, ex-
cept that the loss values are different for the different conditionso
In addition to the non-loaded subscriber loop loss curves, effective loss curves are re-
quired showing, for different lengths and conditions, the losses of loaded trunks and loops,
subscriber loop losses having loops composed of two or more different types of facilities,
current supply losses versus transmitter current and versus loop resistance, transmitting
and receiving losses due to sidetone, terminal junction losses, and many similar curves
useful to the engineer.
LOOP LENGTH IN THOUSANDS OF FEET
,00 0 0 & 0 0 C
R« RECEIVING LOSS
.. T= TRANSMITTING LOSS
SUBSCRIPTS:
Es34V EXCHANGE GRADE
BATTERY SUPPLY.
- Ts 48V TOLL GRADE
BATTERY SUPPLY.
600-OHM REFERENCE TRUNK
/T+l
=-\
S*
<**
\*
12
II
'<>*
III
9 -J
°*
7X
•8
53
4 &
3 J
2
t
0
J
(U
-}
V 2
^
b
^*^
*s
\ 2
^
A-
"V
^
*TT
^
^
^
^^**
^
s^-
TE
^
€
^
^
-
^
^
*~^*'
_£
^
t
2-10-6-6-4-2 0 24 6 & K> 12 14 16 M
EFFECTIVE LOOP LOSS IN DECIBELS
NO. 1 OR NO. 10 MANUAL OR PANEL DIAL OFFICE F1A- AST\
32-BSA CABLE LOOP 635-70«A- AST/
FIG. 13. Effective Transmission Losses in Common-battery Subloops (Courtesy Bell System)
SWITCHBOARD OPERATOR EFFECTIVE TRANSMISSION PERFORMANCE is
also rated by means of the working reference system, except that the reference trunk im-
pedance is 900 ohms instead of the 600 ohms employed for subscriber loop ratings. In
making comparisons, the operator circuit is connected to the reference system in place of
one of the subscriber loops. Since no loop is involved for this connection, single values of
transmitting and receiving losses are adequate for rating each combination of operator's
telephone set circuit and instruments.
The typical values of line and room noise specified for the operator terminal are 45 db
RAP for line noise in the listening ear and 65 db RAP for room noise. The reference
operator receiver (W.E. Co. No. 528) is more efficient than the reference subscriber re-
ceiver (W.E. Co. No. 144) , and the reference room noise for operators is higher than that
for subscribers. Incoming room noise from the distant operator's set also adds to the
overall effective loss in the receiving operator's circuit. The latest design in operator
transmitters and receivers provides improvements in operator transmission which will
permit overall operator to operator standards in the approximate range of 10 to 12 db,
which is comparable with present local subscriber to subscriber plant design.
16. PLANT DESIGN— TOLL
TOLL FACILITIES have been developed, since the earliest open-wire (iron) type, to
include the following: (1) open wire, (2) cable, (3) carrier, and (4) radio.
TOLL OPEN-WIRE FACILITIES consist principally of hard-drawn copper, copper
steel, and high-tensile-strength steel bare wire.
The three gages of hard-drawn copper line wire employed most commonly in Bell Sys-
tem plant are 165, 128, and 104 (mil diameter) wire, the electrical characteristics of which
are shown for various positions and arrangements on the pole line in Fig. 14. For wet
weather the value of g increases and other factors change. Several other gages of copper
line wire are in use in this and other countries, such as 102 mil diameter, but the three
mentioned above are representative of this type of wire usage. Also, a number of basic
wire gages are in use, so that the mil diameter of a given gage of wire, such as No. 8, may
be different under the different basic gages. Figures 15, 16, and 17 show, respectively,
the attenuation frequency characteristics of different gages of hard-drawn copper physi-
PLANT DESIGN TOLL
17-83
5
1
S S $ S S3 S3 & SG S: S S3 Q
»x»»i»\»\xn,uuiiv\u^«4\
SSSSS2SSSSSSS'
S888S88S8SJ
<=>
s s c
re
• a
:-i
I
PQ
§,
f
b
«s i o
.
« H «*- H3
ii
17-84
TELEPHONY
cal (side in Fig. 15) circuits over the voice, type C, and type J carrier frequency ranges,
for both wet and dry weather conditions. The wire spacing and types of insulators
involved are 12-in. and double-petticoat (DP) for Fig. 15, and 8-in. and CS glass for
Figs. 16 and 17. In the frequency range of 20 to 150 kc, the attenuation factor in-
creases rapidly with frequency where the wires are covered with snow or ice. For example,
0 OS 1.0 1.5 2.0 2J 3.O a5 4.O
FREQUENCY IN KILOCYCLES PER SECOND
FIG. 15. Attenuation-frequency Characteristics of Open-wire Side Circuits over the Voice Range
(Courtesy Bell System)
with about 1/3 in. total diameter of melting glaze on a type J, 8 in., CS insulated, 165-
gage carrier pair, the attenuation increases approximately from 0.13 db per mile at 20
kc to 0.9 db per mile at 150 kc. Variations of attenuation with temperature due to re-
sistance change in open wire are about 1 per cent per 4 i/2 deg fahr change from 68 deg
fahr.
In recent years, copper steel wire has been used extensively for telephone circuits, com-
bining strength with relatively low transmission losses and d-c resistance values. This
wire is manufactured with 30 and 40 per cent conductivity, which is the conductivity
ratio (in percentage) of the wire to that of the annealed copper standard of like diameter.
O.22
0.20
0.1S
O.I 6
0.14
0.12
O.IO
0.08
0.06
O.O4
O.02
o
C
^
/
/
&
&s-
/
S^<
^s*'
A
,o&,
//,
^*"
^
/
x
H
^
£*"'
/
/,
xx
^
^
"''
/
^y
y^
f
^
„-***
&
/
/'
^
'''
/
WET WEATHER
— DRY WEATHER
y,
/
s
> 5 10 15 20 25 30 35 40 45 5<
FREQUENCY IN KILOCYCLES PER SECOND
FIG. 16. Attenuation-frequency Characteristics of Open-wire Physical Circuits over the Type C
Carrier Range (Courtesy Bell System)
A 40 per cent conductivity copper steel wire, which is the more commonly used type, has a
steel core with a welded copper casing having a radial thickness of 20 per cent of the total
radius of the wire.
The tensile strength and attenuation of copper steel pairs are about 2 to 2 1/2 times that
of hard-drawn copper of the same size. Owing to higher attenuation, telephone repeaters
PLANT DESIGN — TOLL
17-85
2 0.32
< 0.16
WET WEATHER
DRY WEATHER
40 60 SO 1OO 120 140
FREQUENCY IN KlUOCYCLES PER SECOND
FIG. 17. Attenuation-frequency Characteristics of Open-wire Physical Circuits over the Type J
Carrier Range (Courtesy Bell System)
require closer spacing with copper steel than with hard-drawn copper circuits,
acteristics of copper steel pairs are given in Table 5.
The char-
Table 5. Characteristics of Copper Steel Pairs
(Estimated for 68 deg Fahr — 40 Per Cent Conductivity — 53 Pairs CS Insulators per Mile)
Size of
Fre-
Resist-
Inductance,
mh per pair
Tnile
Characteristic
Impedance, Dry, ohms
Attenuation,
db per mile,
dry
Attenuation,
db per mile,
wet
Wire,
mil
diameter
kc
ohms
Pin Spacing
Pin Spacing
Phi Spacing
Pin Spacing
8 in.
12 in.
8in,
12 in.
Sin.
12 in.
8 in.
12 in.
165
0.2
9.9
3.125
3.385
761-J516
793-J542
0.057
0.054
0.063
0.060
1.0
10.3
3.060
3.320
572-/I43
615-jl43
0.078
0.073
0.084
0.078
3.0
10.8
3.027
3.287
558 -j 51
597 -j 51
0.085
0.079
0.092
0.086
10.0
11.4
2.995
3.255
552 -j 16
592 -j 16
0.092
0.085
0.104
0.098
30.0
12.6
2.986
3.246
551 -j 6
591 - j 6
0.103
0.095
0.127
0.120
140.0
24.7
2.974
3,234
550 -j 2.4
590 -j 2.4
0.207
0.192
0.282
0.273
128
0.2
16.6
3.285
3,545
943-J736
991 - ;759
0.077
0.073
0.084
0.081
1.0
17.3
3.250
3.510
635-;230
674-J232
0.120
0.112
0.126
0.119
3.0
18.0
3.206
3.466
593 _ j 86
634 -j 86
0.134
0.124
0.142
0.132
10.0
18.7
3.167
3.427
583 -j 27
625 - j 27
0.142
0.131
0.155
0.145
30.0
19.7
3.148
3.408
580 -j 9.4
623 -j 9.4
0.152
0.139
0.177
0.168
140.0
30.5
3.139
3.399
580 -j 3
622 -j 3
0.241
0.224
0.321
0.310
104
0.2
25.0
3.430
3.690
1139 -;958
1189 -J988
0.096
0.091
0.105
0.101
1.0
25.7
3.410
3.670
691 - J324
736-J328
0.162
0.152
0.169
0.160
3.0
26.6
3.357
3.617
621 - j\24
666-J124
0.188
0.174
0.1%
0.183
10.0
27.7
3.313
3.573
606 -j 40
651 -j 40
0.201
0.186
0.215
0.200
30.0
28.7
3.287
3.547
602 -j 14
647 - j 14
0.211
0.195
0.238
0.224
140.0
37.6
3.277
3.537
602 -j 3.8
647-; 3.8
0.284
0.264
0.367
0.353
Notes:
1. Resistance (d-c) is 0.1 ohm less than resistance at 0.2 kc for all three gages.
2. Leakage conductance and capacities of copper steel pairs are comparable to those of same size hard-drawn copper
pairs (Fig. 14).
3. For DP insulators the attenuation change from dry to wet weather conditions is about twice that for CS insulators.
4. The above estimated values will vary somewhat from actual measurements, owing to the effects of transpositions,
spacing, and other small irregularities, which cannot be calculated. For 12-In. pairs, assume on the average about
10 per cent lower high-frequency impedance and about 10 per cent higher high-frequency attenuation values. The
deviations should be less for the closer spaced pairs with point-type transpositions. (Courtesy Bell System.)
17-86
TELEPHONY
HIGH-STRENGTH STEEL WIRE has practically replaced the various grades of iron
(E.B.B. and B.B.) and mild steel wire for telephone purposes because of its greater strength
and coordination with other wire services. The high-strength steel wire now in production
by several manufacturers is used for only the very short toll circuits in some parts of the
country, on account of its high attenuation and inherent noise characteristics. Its prin-
cipal usage is in exchange plant. Steel wire is now generally zinc coated (galvanized)
electrolytically, which insures a more uniform coating than the "hot dip" process. The
usual weights of zinc coating vary from 0.8 to 2.4 oz per sq ft, depending upon the custom-
er's requirements. The characteristics are given in more detail in article 17, Plant De-
sign— Exchange.
CABLE FACILITIES for toll purposes comprise a number of types of loaded and non-
loaded cable pairs. Toll entrance cables are employed for extending open-wire toll lines
into toll or toll terminal
Table 6. Load-coil Spacings offices or stations for dis-
tances usually limited to a
few miles. Toll cables are
employed as permanent
backbone toll plant, inter-
connecting principal cities
and important intermedi-
ate switching and equip-
ment centers. Toll and
toll entrance cables may
be of the aerial or under-
ground type or combina-
tions of both, but the
tendency is to place them
underground for greater
reliability of service.
Cable facilities, being
*For side and phantom cable capacitances of 0.062 and 0.102 /*£ necessarily of small-gage,
Code
Designation
Nominal
Spacing,
feet
General Application
A
700*
Cables serving open-wire carrier.
B
3000*
Cables serving open-wire carrier. Toll and
exchange cables.
C
929*
Cables serving open- wire carrier.
D
4500*
Exchange cables.
E
5575*
Toll entrance cables. Replaced by H,
except when used with C spacing.
F
2787*
Cables serving open-wire carrier (phantom
circuits).
H
6000*
Toll, toll entrance, and exchange cables.
J
600 t
Cables serving J open-wire carrier.
X
680*
Equivalent capacity in carrier office cables.
Y
2130 *
Equivalent capacity in carrier office cables.
per mile, respectively.
t For physical pair capacitance of 0.025 /if per mile.
soft-drawn, insulated cop-
per conductors, in order to
provide economical sizes
of conductor complements, have relatively high mutual capacitances, resistances, and
greatly increased attenuation per mile over the larger-gage, wider-spaced, open-wire con-
ductors. Figure 18 shows the characteristics of standard types of paper-insulated cable
telephone circuits at 1000 cycles per second, as used in the Bell System. In column 2 of
Fig. IS, the abbreviations N.L.S. and N.L.P. refer to non-loaded side and non-loaded
phantom respectively, while the remaining abbreviations show the load coil spacing by
letter (H-6000 feet and B-3000 ft), the inductance in millihenries by the figure, and whether
the circuit is a side or phantom by the letters S and P respectively. For a designation
such as H-44-25, the first
and second figures refer to Table 7. Toll-entrance Cable Loading
the side and phantom coil
inductances, respectively.
The type of loading at
present employed in toll
cables for four-wire voice
frequency message cable
circuits is usually the 19-
gage H-44-25 or H-88-50
type, since less variation
in attenuation over the
voice range and higher
cutoff frequencies are ob-
tained with these loadings
(Fig. 18) than are possible
with the older, higher-
inductance-type loading. Repeaters generally are spaced at 40-50 mile intervals. For
two-wire voice-frequency message cable circuits, 19-gage H-88-50 or B-88-50 loading is
usually employed. The variation in attenuation over the voice range is small, the cutoff
frequency is amply high, and telephone repeater spacings of about 40-50 miles generally
are used.
For program transmission (article 18) 16-gage B-22 loaded cable pairs were specially
Carrier
Frequency
Range, kc
Type of Loading
0- 10
0- 30
0- 30
0-145
0-145
0-145
0- 30
0- 10
B H-15-15 (B for side, H for phantom)
C E-4.1-12,8 (C for side, E for phantom and 1 65 open-
wire circuits, 1 2 in.)
C E-4.8-1 2.8 (C for side, E for phantom and 1 28 or 1 04
open-wire circuits, 1 2 in.)
J-0.72 1 65 open-wire, 8 in. i Used with disk-insu-
128 open-wire, 8 in. I lated pairs in
J-0.85 1 28 open-wire, 8 in. | shielded, spiral-four
J-0.94 104 open-wire, 8 in. J quadded cable.
X-2.7 Office cable loading.
Y-9 Office cable loading.
PLANT DESIGN TOLL
17-87
S-S eg
§3
«^^^«^^«jocjvoo::or::£;o^:aoo?j;Q-^.S^-^:£2::2:2:jr
S|
11
S&b
Hg^
^°
— 0
i=S
lil
?
S'S
-§1 1
&
•5
.vOinr^o4^(Ntrv .vOxncAMcsr^m . vo ^ -r «% <M rsi ^ .vo^-rm^t-on--
55 ^*
o DD
-5 s _
"o 8 g
U
11 §
£2 x
or* SS
j
sOf^O-«-00000'fl-TnO-«-OOCOO — r^O'«-c^OoooO-9-0'«-cnoeooo
E^ I
> 2 a
b . %
« 2 o
, .
go 9-
S*J3
|>*|
§
ocoocnt^oivn^i^So^t^mS — JRSSSt^tQ^SS — S^SSSSo
&0 -T!
^ J^
a
NO^O"^ooooo^rcno'*-ooGOO--«no-9-c^csoooo-<ro-<rf^ooooG>
gj tn
I
*bO £ I
J1 1
^0 S
§
! ~s
rt so '
11 o
J (2
<D
io,
-0**.^*~^*<**°**-~^™
11 §
fl
3
II
^~^^T^^^^^^ _,_^«
g * *»
°ic *
S'S S
e § *3
ooc^oooo.nt-.vovo^-oo^^csr^ o^^oo^oxt^r^o-s-^eotrtvo^nosov
l-s I
1- 5
«.
Si *2
o3 » faC
o>
^"3 §
S ^3
*§ a
S-cs &
£° 1
«
5|g*SSSSSS|g22£S22g^SSSSSSSgS22~Sg
— S "S
J 3 H
0
.2| 1
o
g0 0
>^=! T3
«,«
oS
Bfl S
'^ |
si |
*t
|l -I
e3 o ij
fiv2
2 u
<=>
|| I
u
s
t^* r^t
°"S P4
15 1
^-°
2"C
J
oo
§| . g
S ^ CH
6g
i
co^^Ncno^^-^^xrt^cn^^^--^rst«-^^o^oo^^«o^--
l|l -s
o
.Moa,oo^W«-,W^**W-,*««««««««^
W1
ol
£
^J?SS?:^S ^^SS^^S °°^SS5^S °°JQSS^^SS
111 ?
33 s
'sfe-B
-d
0
H2 1
O » o
w to GJ
-s-Sce
.8
^-.^o-in^ r mo-^c^ rr-t^ «»Ai^ -n-- r ««r^$
2 © o .25
g1!^ ^
J-3
)— 1 tc
*"-§
«*«-2^5- c.^^o^t. r^^^co^^ nm^aor^-
^>| §
&2 ® J-
o i ® s
i-s-i
^8
xzzzzzs SSJRSSSS SRS«SS«S »»aas»ss
i£l d
fe .2
M.s>3
OS
^1 a
«•
j
§3^ g
If ^ s
«i
£|
q
•K^
O^OsOsO^ONO.Os<^NONOvOvO^ONO>ONOl^C^^ONavOvOvONNOvONONO^NONO^
d!
^0
17-88
TELEPHONY
developed to give a high cutoff frequency. These facilities are capable of transmitting a
frequency band up to about 8000 cycles without serious distortion.
Figure 19 shows the attenuation frequency characteristics of various types of cable
circuits loaded for voice frequency and program service.
Table 6 gives the code designations of load coil spacings as devised for Bell System use.
x**
19 GAUGE H-I74-106
CIRCUITS
/
S^
.— •"
^
SID
E X*
/
(-"
,x---
PHAf
slTOM
/-
•* •—
_- — • -
^*.**
>HAh
.x
mDM
1
19 GAUGE H-44-25
CIRCUITS
j 0 0.5 1.0 1.5 2.O 2.5 3.0 3.5 0 0.5 1.0 1.5 2.0 2.5 3.0 3.5 4.0 4.5 5.0
SIDE
19 GAUGE H-88-50
CIRCUITS
O 0.5 1.0 4.5 2.0 2.5 3.0 3.5 0 0.5 1.0 1.5 2.0 2.5 3.0 3.5 4.0 4.5 5.0
/
SID
^
E/
/ /
^ — •
— — •
-^ .^*
.. ^TPHAh
JTOM
16 GAUGE B-88-5O
CIRCUITS
1 i 1
5 6 70 1 23 4 5
FREQUENCY IN KILOCYCLES PER SECOND
PIG. 19. Attenuation-frequency Characteristics of Various Types of Loaded Cable Circuits (Courtesy
Bell System)
The type of loading generally used in toll entrance cables is of the H-31-18 type for voice-
frequency circuits and of the types shown in Table 7 for carrier circuits.
Non-loaded cable facilities are employed in both toll entrance and toll cables. Such toll
entrance facilities may be used without appreciable transmission penalty up to about
3000 ft in extending open-wire circuits into offices or intermediate toll equipment points.
For K carrier systems, which are operated through toll cables, only non-loaded pairs may
be used, since loading is not available for the K frequency range. For J carrier systems a
specia% designed low-capacity, 16-gage, spiral-four loaded or non-loaded cable may be
used for entrances.
PLANT DESIGN — TOLL
17-89
Cable faculties used for toll purposes have, in general, been composed of 10-, 13-, 16-,
and 19-gage cable conductors, paired and quadded for physical and phantom circuit oper-
ation. Some non-quadded cables for physical circuits only have been used. At present
19 gage is largely employed, but in a few cases 16 gage may be added. The newer toll
cables have the short pair twist, high dielectric strength, core to sheath, and nominal
mutual capacities of 0.062 and 0.096 /if per mile for side and phantom respectively. The
standard sizes of toll and toll entrance cable cover a wide range of standard numbers of
quads and pairs, and several different gages may be placed in the same lead cable sheath,
including pairs for exchange use, as required to meet service needs.
Toll entrance cables for carrier, non-phantomed, open-wire lines have the long pair
twist and nominal capacities of 0.062 and 0.102 juf per mile for the side and phantom,
respectively.
Variations in net losses in cable facilities due to temperature changes are shown in Fig.
20.
Loading
Loss at 55 Deg Fahr, decibels per mile
22-gage
19-gage
I6-gage
13- or 14-
gage *
10-gage
B-22-N
B-44-N
B-88-50-S
B-88-50-P
H-22-N
H-44-25-S
H-44-25-P
H-88-50-S
H-88-50-P
H-172-63-S)
H-174-63-SJ
H-172-63-P)
H-174-63-PJ
H-174-I06-S
H-174-106-P
0.45
.34
0.236
0.157
a. so
.42
.28
.23
.62
.47
.39
.35
.30
.27
.28
.28
.22
.16
.14
.32
.25
.21
.19
.16
.16
.16
.16
.13
.92
.77
.66
.56
.49
.51
.50
.40
.14
.115
.12*
0.08
.07
.10
.084
* Value marked with * applies to 14-gage.
Loading
± Variations from Loss at 55 Deg Fahr, decibels per mile
22-gage
19-gage
I6-gage
Aerial
Cable *
U.G.
Cables t
Aerial
Cable *
U.G.
Cable f
Aerial
Cable *
U.G.
Cable f
B-22-N
B-44-N
B-88-50-S
0.052
.040
.031
0.017
.013
.011
0.028
0.009
0.060
0.020
.018
.006
B-88-50-P
H-22-N
H-44-25-S
H-44-25-P
.050
.017
.026
.071
.055
.046
.009
.024
.018
.015
.015
.037
.029
.024
.005
.012
.010
.008
.110
.092
.037
.031
H-88-50-S
H-88-50-P
.079
.067
.026
.022
.041
.035
.014
.012
.022
.019
.007
.006
H-172-63-S1
H-174-63-SJ
.059
.020
.031
.010
.018
.006
H-172-63-P)
H-174-63-PJ
.061
.020
.032
.011
.018
.006
H-174-106-S
H-174-106-P
.060
.048
.020
.016
.032
.025
,011
.008
.017
.013
.006
.004
* Temperature range, ±54 deg fahr; resistance variation, ±12 per cent
f Temperature range, ±18 deg fahr; resistance variation, ±4 per cent
FIG 20 Net Loss Variations with Temperature for Different Gages and Loadings of Cable Circuits
(Courtesy Bell System)
17-90
TELEPHONY
The cables may have a plain lead sheath covering with no outer protection, or, if pro-
tection is required from gophers, digging, or other extraneous disturbances, the sheath
may be covered with jute, gopher and jute protection, corrosion protection, or tape armor
for either aerial or buried construction. Submarine cables have single or double armored
protection, composed of heavy steel wires laid around the sheath with jute and compound
in one or two layers. Metallic shields are also used, as required, around the cable core,
individual groups or quads of cable conductors, to protect circuits from electrical dis-
turbances.
CARRIER FACILITIES may be provided in either open wire or cable. For any given
carrier system between two points, the facilities selected must be suitable for that system.
Low-frequency carrier systems of the G and H types generally employ 12-in.-spaced, open-
wire facilities, having voice-frequency characteristics, except that, as the number of these
systems increase on a given pole line, a carrier transposition scheme may be required to
limit crosstalk, since the usual voice-frequency schemes are not designed for the higher
frequencies. The C carrier system generally employs 12- or 8-in.-spaced, open- wire
facilities, transposed for frequencies up to 30 kc, although the physical pairs or phantom
groups may be transposed one at a time, according to the selected transposition scheme,
as required to provide for the carrier systems on the given pole line. The J carrier system,
being in the high-frequency group, requires 8- or 6-in.-spaced, open-wire facilities specially
transposed to limit crosstalk at frequencies up to 140 kc.
With the G, H, and C systems, DP insulators and transposition drop brackets are usu-
ally satisfactory for wet or dry weather, but for the J system it is necessary to provide
CS insulators and point-type transpositions, where the pole line will initially or ultimately
have a full complement of carrier systems. Wire sag must be limited to small deviations
from normal and all other physical irregularities must be controlled where carrier systems
are operated. These limitations assume greater importance as the system frequency in-
creases.
The K carrier system, operating through cable only, requires suitable conductors. Non-
loaded pairs of 0.062-juf capacity per mile and of 19 gage, selected as the most economical
gage, must be properly balanced in the cable mutually and against other facilities and
segregated (using separate cables or layer shields) for the two directions of transmission.
Figure 21 shows the attenuation-frequency characteristics of 19-gage non-loaded cable
circuits over the K carrier range at different temperatures.
4.2
4.0
3.8
3.6
i«
uj 3.2
a.
3 3-0
UJ
00
2.6
2.4
gx
8 12 16 20 24 28 32 36 40 44 48 52 56 6O
FREQUENCY IN KILOCYCLES PER SECOND
FIG. 21. Attenuation-frequency Characteristics of Non-loaded 19-gage Cable Circuits over the Type K
Carrier Range at Different Temperatures (Deg Fahr) (Courtesy Bell System)
COAXIAL CABLE is required for L carrier system operation, on account of the high-
frequency range of this system (up to possibly 7 Me or more). This type of cable, first
installed commercially between Minneapolis, Minn., and Stevens Point, Wis., in 1941, is
built up of multiples of two coaxial tubes or units, plus ordinary paper-insulated con-
ductors as needed to take care of requirements for short-haul message circuits and signal-
ing and alarm trunks.
PLANT DESIGN — TOLL
17-91
The Stevens Point-Minneapolis cable
contained four coaxial units, with two
22-gage pairs in the center, a 19- and
22-gage pair in each of the four outer
interstices between the units, and eight-
een 19-gage quads surrounding this as-
sembly. Since that installation many
changes and improvements have been
made in the design and construction of
coaxial cable. One of the latest designs
provides for 8 coaxial units and about
78 quads of 19-gage copper equivalent,
built in with, and surrounding the units
to form a full-size lead-sheathed cable,
The quads may be used for message and
program service, order wires, alarms, and
miscellaneous applications, and the co-
axial units for message, television, and
possibly other services.
The present coaxial unit consists of a
X
60
200 400 600 1000 2OOO 4OOO
FREQUENCY JN KJLOCYCLES PER SECOND
FIG. 22. Attenuation-frequency Characteristics of an
0.375-in. Longitudinal Seam Coasiai Cable Circuit
(Courtesy Bell System)
Z76!
single 12-mil copper tape (outer conductor) formed into a tubular conductor, which is, in
turn, tightly wrapped with two 6-mil steel tapes, the outer of which covers the gaps be-
tween the turns of the inner steel tape.
Each edge of the copper tape has small
serrations which engage the opposite
edge of the copper tape, and the two
edges thus interlock to form a tube.
This design is known as "longitudinal
seam" coaxial. A 10-gage (100.4-mil)
copper wire (inner conductor) is sup-
ported in the center of this tube by
polyethylene disks (0.085 in. thick),
spaced about 1 in. apart.
The inside diameter of the present
standard coaxial tube is 0.375 in. (an
original design employed a 13-gage cen-
tral conductor and an outer conductor
having an inside diameter of 0.27-in.).
Attenuation and impedance character-
istics are shown in Pigs. 22 and 23. The
new type permits lengthening auxiliary
repeater spacings from about 5.4 miles
(for the 0.27-in. tube) to about 7,9 miles
O-2
5
X-3
2OO -4OO 6OO KXXJ 20OO 4OOO
FREQUENCY D4 KILOCYCLES PER SECOND
FIG. 23. Impedance Characteristics of an 0.375-in.
Longitudinal Seam Coaxial Cable Circuit (Courtesy
Bell System)
(for the 0.375-in. tube), with 480 circuits provided in each case. Also the maximum spac-
ing between main repeater stations is increased from about 90 to more than 150 miles.
The larger coaxial will transmit from 1.5 to 2 times as wide
a frequency band as the smaller coaxial, assuming the same
repeater spacings, thus permitting the handling of high
definition or color television if the demand for it arises.
Figure 24 shows construction of an eight-unit coaxial with
a complement of wire quads.
Lightning protection for the complete cable is provided
by placing a 10-mil, corrugated, copper jacket over the
lead sheath of the cable, which is first wrapped in thermo-
plastic material and a layer of tough cloth. The copper
jacket is then covered with cloth tape.
Each regular coaxial unit is paired with an identical
alternate coaxial unit, which is automatically switched
into service, replacing the regular unit, in case of fault
occurrence.
PHANTOM CIRCUIT operation is common in both
open wire and cable. Two open-wire physical circuits or
two cable pairs, which are twisted together to form a quad
(four wires) , can be equipped at their terminals to provide
a third circuit, called a phantom, as shown in Fig. 25.
An 8-unit Coaxial
2.
§tment
tesy Bell System)
17-92
TELEPHONY
The side-circuit currents circulate over the side circuits as shown by the dashed arrows,
and the phantom-circuit currents circulate over the phantom circuit as shown by the
solid arrows. The line sides of the phantom repeating coils are closely balanced with
respect to the phantom tap so that the phantom-circuit current, dividing about equally
Office A Una Office B
Repeating
Coil
Wire No. 1
Repeating
Coil
>, g
Side Circuit 1
,<- * «=
if
^._. ^ Wire No. 2
41
!| Side Circuit
— = — '
Phantom Circuit
— ^^n
Wire No. 3
Phantom Circuit
Side Circuit f
1
_^_ « Wire No. 4
•f]
s
,
-
3. Side Circuit
3
< — instantaneous direction of side-circuit currents.
< instantaneous direction of phantom-circuit currents.
FIG. 25. Phantom Circuit Derived from Two Side Circuits
between the two wires of each pair, causes no appreciable induced current in the side-
circuit terminations. Also, the side-circuit currents do not enter the phantom. This ar-
rangement provides three circuits from four wires but requires a well-maintained balance
in the line sides of the repeating coils and between the four wires, and adequate trans-
posing, both in the open-wire group and the cable quad, to prevent excessive noise and
crosstalk.
17. PLANT DESIGN— EXCHANGE
Exchange facilities, employed in connecting subscriber station equipment with central
offices, for interoffice trunking in multioffice exchange areas, and for miscellaneous uses,
may consist of cable or open wire or a combination of both types of facilities. The latest
Gage Cabl
e
26
24
22
19
16
13
Type of cable. . . . J
ST
AST
BST
M
SM
ASM
GSM
DSM
NM
SA
ASA
BSA
CSA
NA
ANA
TA
TS
BNB
CNB
TB
ANB
DNB
TH
NH
TJ
R, ohms per mile at
68° F
440
.069
440
.079
274
.072
274
.084
274
.065
171
.082
171
.073
171
.062
171
.068
85
.084
85
.066
42
.066
21.4
.066
C, Atf per mile
Loading
Load
Spacing,
feet
Decibels per Mile at 68 Deg Fahr
B-175
B-I35
B-88
D-175
D-135
D-88
H-250
H-175
E-135
H-88
E-44
M-175
M-135
M-88
R-133
Non-
loaded.
3,000
3,000
3,000
4,500
4,500
4,500
6,000
6,000
6,000
6,000
6,000
9,000
9,000
9,000
11,600
.94
1.05
1.30
1.12
1.25
1.52
.01
.12
.39
.20
.33
1.62
.63
.69
.87
.74
.82
KOI
.68
.75
.94
.80
.88
1.09
.44
.48
.25
.26
.22
.24
.14
.14
.60
.51
.56
.70
.49
.34
.28
.30
.38
.30
.25
.27
34
.18
.15
.26
.27
.30
.38
.50
.33
.36
.44
.41
1.11
.17
.15
.16
.21
.27
.17
.20
.24
.21
.75
.11
.10
.11
".\4
.12
.50
.31
.34
.42
.56
1.40
1.69
2.06
1.50
1.80
2.21
.92
1.14
1.46
.00
.23
.58
.63
.79
1.04
.60
.65
.60
63
1.63
1.91
1.75
2.04
1.09
1.31
.18
.42
1.14
1.25
.75
.92
.73
.87
.41
.49
76
80
2.67
2.86
2.14
2.31
2.04
1.79
1.69
1.55
1.63
1.26
PIG. 26. Attenuation Losses of Non-quadded Exchange Area Cable Facilities
PLANT DESIGN — EXCHANGE
17-93
developments affecting rural service include (1) trial installations of telephone carrier
systems on rural power distribution lines, serving areas where telephone facilities are not
available, and (2) direct radio channels between the central office and farm or ranch homes
heretofore economically inaccessible for the usual pole line and open-wire construction.
EXCHANGE CABLES, in general, employ five different gages of soft-drawn copper
conductors, namely, 26, 24, 22, 19, and 16 gage. A relatively small amount of 28-gage
cable, developed to conserve copper during World War II, has been manufactured, but
with normal copper prices its use in place of 26-gage, where applicable, does not effect
appreciable cost savings. Exchange trunk cables are usually of 19 or smaller gage.
Type of Facility
Values Shown Are
R
(Loop),
ohms
(dc)
L.
henrys
<?,
mhos
(1000
cycles)
(X1Q-6)
c,
farads
(X10~6)
G
C
Per Unit
Length of
At
Temp
ofF°
Dry
or
Wet
Non-quadded exchange area cables
*"• I ST %
f M SM ASM GSM
24 gage { DSM
I NM
{SA ASA BSA CSA
NA ANA
TS
19jra*e I BNB CNB
iv gage { TB j^ I)NB
16 gage TH NH
13 gage TJ
Mile
68
68
68
68
68
68
68
68
68
68
68
68
68
440
440
274
274
274
171
171
171
171
85
85
42
21.4
0.001
.001
.001
.001
.001
.001
.001
.001
.001
.001
.001
.001
.001
1.8
2.1
1.9
2.2
1.7
2.1
.9
.6
.7
2.2
.7
.7
.7
0.069
.079
.072
.084
.065
.082
.073
.062
.068
.084
.066
.066
.066
26
26
26
26
26
26
26
26
26
26
26
26
26
Submarine cables — non-quadded
[24 gage
Single paper insulation s 22 u
119 «
f24gage
1 "yy K
Double paper insulation <** u
U6 *
Mile
55
55
55
55
55
55
55
266
166
83
266
166
83
41
.001
.001
.001
.001
.001
.001
.001
.7
.9
2.0
1.8
2.1
2.2
1.7
.066
.075
.078
.071
.080
.083
.066
26
26
26
26
26
26
26
17-gageUWire
U bridle -wire
_ . \ distribution wire (buried)
Eibfoot
fEIofoot
I mile
68
68
68
Wet
10.3
10.3
54
,00033
.00027
.0014
*
7.6
40.0
.025
f.023f
1.026J
f J22t
I.135t
328 f
2961
328 f
296*
Drop wires
{g^
{&*?
14 gage EC type
Eolofoot
68
68
68
68
68
Wet
51
51
28
28
5
.00021
.00023
.00022
.00022
.00025
*
*
*
.042
.036
.040
.040
.041
Miscellaneous wires and cables
Inside wiring cable — 22 gauge
f OR type
TT> «
Service cables— 22 gage \^ u
LR
ITR u
AL wire 14 gage
Bridle wire 20 gage
Duct wire 22 gage )
DTJ station wire 22 gage /
GN station wire 22 gage
Kilofoot
};
«
u
68
68
68
68
68
68
Wet
37
37 §
5
21
33
33
.00020
. 00027 §
.00029
.00028
. 00030 B
. 00030 f|
*
*
*
*
*
*
,025
.0205
.033
.036
.033 |!
.048 fi
* Leakage conductance at 1000 cycles is negligible as compared with capatitive susceptance,
t Initial values after one day soaking in water.
j Estimated values after 5 to 10 years in ground, depending upon moisture conditions in soil
§ These values may be applied to both one and two pair cables,
j These values are satisfactory for pairs, triples, or quads.
FIG. 27. Primary Distributed Constants of Cables 'and Miscellaneous Paired Conductor Facilities
17-94
TELEPHONY
Cable
Loading
Propagation Constant at 68 Deg Fahr
Characteristic Impedance *
at 68 Deg Fahr
Gage
Code
Per Mile
Per Kilofoot
26
ST
AST
NL
B-175
B-135
B-88
,3072 + ; .3105
.1084 + ;' .9354
.1207+; .8223
.1492+; .6713
.05818 +;. 05881
. 02053 +;M772
.02286 + /.1557
.02826 + ;. 1271
718 -;706 = 1007 \~44755
2204 -;251 - 2218rT"5*
1929 -;28I = 1949 r~O*
1567 -;344 « 1604VT2T?5
D-175
D-135
D-88
H-135
.1286+; .7739
.1434 + ; .6824
.1747 + ; .5644
.1615+; .6030
. 02436 +;M466
.02716+;. 1292
.03309 +;M069
.03059 + ;M142
1848 -;299 - 1872\~Tr
1618 - ;332 = 1652 \TT765
1325 - ;403 = 1385^1679^
1440 -;383 « 1490VT4T9*
H-88
H-44
M-135
M-88
.1940 +;' .5049
.2375+; .4062
.1880 + ; .5153
.2196+; .4424
.03674 +;. 09563
.04498 +;. 07693
.03561 + ;. 09759
.04159 +;. 08379
1192 - ;453 = 1275\"20.86
949 -;552 « 1 098 \ 30. 2^
1257-;460 « 1338^0^
1057 -;525 « IISOVIO5
BST
NL
B-175
B-135
B-88
.3287 + ; .3322
.1160+;!. 0009
.1292 + ; .8799
.1596 + ; ,7183
.06225+;. 06292
. 02197 +;M896
.02447+;. 1666
.03023 +;.1360
672-;660= 942V44T35
2060 ~;235 « 2073 \ 6^
1802 -;263 « 1821 \ 8. 3*
1464-;322 = 1499M2.45
D-175
D-135
D-88
H-135
.1376+; .8281
.1534 + ; .7302
.1869+; .6039
.1728+; .6452
.02606 +;M568
.02905 +;. 1383
.03540 +;M144
.03273+;. 1222
1727-;280 = 1750\" 9.2d
1512~;310 « 1544\11,6°
1238-;376 = 1294\16.9°
1346»;358 = 1393\ 14.9°
H-88
H-44
M-135
M-88
.2076 + ; .5403
.2541 +; .4346
.2012 + ; .5514
.2350 +; .4734
.03932 +;. 1023
.04813+;. 08231
.03811 +;M044
.04451 +;*. 08966
1H4 -;423 = 1192\20.8°
887 - ;516 - 1026\30.2°
1174 ~;430 = 1250\20.1°
988 - ;490 » 1103\26.4°
24
M
SM
ASM
CSM
NL
B-175
B-135
B-88
.2467+; .2513
.0722 + ; .9504
.0794 +;' .8344
. 0998 + 3 . 6757
.04672 +;. 04759
. 01367 +j. 1800
.01504 +;M580
.01890 +;. 1280
558-;542= 778 \ 44. 2°
2155 -;155 = 2161\ 4.1°
1880 -;171 = 1888\ 5.2°
1515 - ;216 * 1530\ 8.1°
D-175
D-135
D-88
H-135
.0849+; .7844
.0941 +; .6887
.1165 + ; .5613
.1063+; .6035
.01608+;. 1486
. 01782 + /.1304
. 02206 +;M063
.02013+;.! 143
1800 -;186 = 1810\ 5.9°
1566-;209 = 1580\ 7.6°
1264-;257 = 1290\il.5°
1386-;239 = 1407 \ 9.8°
H-88
H-44
M-135
M-88
.1309+; .4945
.1682 +; .3763
.1254 + ; .5066
.1513+; .4212
.02479 +;. 09366
.03185 + ;. 07127
.02375 +;. 09595
.02866+;. 07977
1123 -;292 « 1160\ 14.6°
844-;372= 922 \ 23. 8°
1187 -;294 = 1223\13.9°
968 -;345 = 1028\ 19.6°
DSM
NL
B-175
B-135
B-88
.2664+; .2715
.0780 + ; 1.0266
.0858 +; .9013
.1078+; .7298
.05045 +;.05142
.01477+;. 1944
.01625 + ;.1707
.02042+;. 1382
517-;503« 721 \ 44. 2°
1996 -;143 = 2001 \ 4.1°
1741 - ;158 - 1748\ 5.2°
1402 - ;200 = 1416\ 8.1°
D-175
D-135
D-88
H-135
.0917 +;" .8473
.1016 +; .7439
.1258+; .6063
.1148+; .6519
.01737 + ;. 1605
.01924 +;M409
,02383 + ;. 1148
. 02174 +;M235
1667 -;172 » I676\'5.9°
1450 -;193 = 1463\ 7.6°
1170 -;238 » 1194\ 11.5°
1284 -;222 = 1303\ 9.8°
H-88
H-44
M-135
M-88
.1414 +;* .5341
.1817+; .4065
.1354+; .5472
.1634+; .4550
.02678 +;M012
.03441 +;. 07699
. 02564 +;M 036
.03095 + ;. 08617
1039 -;271 « 1074\14.6°
781-;345= 854 \ 23. 8°
1099-;272= 1132\ 13.9°
a97-;319= 952 \ 19. 6°
NM
NL
.2342 +;' .2388
.04436 + ;. 04522
588 - ;572 - 820 \44.2°
* Mid-section iterative impedance in cases of loaded facilities.
FIG. 28. Secondary Constants of Exchange Area Cable Facilities at 1000 Cycles per Second — 26 and
PLANT DESIGN — EXCHANGE
17-95
Cable
Loading
Propagation Constant at 68 De& Fahr
Characteristic Impedance *
at 68 Deg Fahr
Gage
Code
Per Mile
Per Kilofoot
22
SA
ASA
BSA
CSA
NL
B-175
B-135
B-88
.2065+y .2134
. 0503 +yi. 0155
.0549 + y .8900
.0689+y .7177
.03911 +y. 04042
. 00953 +y. 1923
.01040 + j.l 686
. 01305 +y. 1359
416-y399~ 576 \ 43. 8°
2025 -j 92 =» 2027 \ 2.6°
1762-jl02» 1765V 3. 3°
1414 -yi30 = 1420 \ 5.3°
D-I75
D-I35
D-88
H-I35
.0583+y .8365
.0647+j .7325
.0808+j .5922
,0729+y .6402
. 01 104 +y. 1584
.01 225+ j.l 387
. 01530 +J.1122
.01381 +y.!213
1694-yil3« 1698V 3.8°
1465 - yi25 = 1470\ 4,9°
1170 -yi56- IISOV'O5
1298-yi44« 1306\ 6.3°
H-88
H-44
M-135
M-88
.0907+y .5185
.1199+y .3796
.0863+y .5333
.1060+j .4341
. 01718 +J.09820
.02271 +y. 07189
. 01634 +J.1010
. 02008 +y. 08222
1036- J177- 1051 rO3
748-y233 = 783 \ 17. 3°
1109 -yi78- 1123\ 9.1°
879-j214= 905\13.7°
NA
ANA
NL
.1946 + j .2012
.03686 +y. 03811
442-j424= 612 HO5
TA
NL
.1792+j .1853
. 03394 +j. 03509
479-j460- 664 \ 43. 8°
TS
NL
.1882 +j .1945
. 03564 +j. 03684
457 _ j438 = 633 \43.8°
19
BNB
CNB
NL
B-135
B-88
.1446+y .1551
,0304+j .900
.0386+j .725
.02739+;. 02938
.00576+ j.l 705
.00731 + J.1373
295-j273= 402 \ 42. 8°
1741 -j 52= 1742\ 1.7°
1393 -j 69- 1395\ 2.8°
D-175
D-135
D-88
H-135
.0321 +y .8457
.0349+j .740
.0439+j .5957
.0388 +y .6455
. 00608 +j. 1602
.00661 + j. 1402
.00831 +j. 1128
. 00735 +y, 1223
1676 -j 58 - 1677\ 2.0°
1448 -j 63* I449\ 2.5°
1155 -j 81 = I158\ 4.0°
1281 -j 74- I283\ 3.3°
H-88
H-44
M-88
.0487+j .5194
.0645+j .3701
.0568+j .4302
. 00922 +y. 09837
. 01222 +j. 07009
. 01 076 +j. 08148
1013 ~y 92= 1017\ 5.2°
713 -j 122= 723\' 9-7°
854 _ .fin . 861 rr^
TB
ANB
DNB
NL
B-175
B-135
B-88
.1282+y .1375
.0254+y .908
.0270+y .795
.0342+j .641
. 02428 +j. 02604
.00481 +y. 1720
.00511 + /.1506
. 00648 +J.1214
333-j308= 453 V4O5
2237 -y 54= 2238 FT?5
1951 _ j 61 = 1952\ 1.8°
1563 -j 76= 1565 \~2TF
D-175
D-135
D-88
H-175
.0282+y .7461
.0310 +j .653
.0390 + y .5269
.0315+y .6507
. 00534 +j. 141 3
.00587+ j.l 237
. 00739 +/. 09979
.00597 + J.1232
1862 — j 65 = 1863 \ 2.0°
1618 -y 71 * 1620\ 2.5°
1292 -j' 91 = 1295^^0*
1643 -j 75 = 1645\ 2.6°
H-135
H-88
H-44
M-88
.0345+y .5694
.0432+j .4590
.0571 +y .3282
.0505+y .3796
.00653 + J.1078
. 0081 8 +j. 08693
.01081 + J.06216
. 00956 +j. 071 89
1423 -j 82= 1425 \ 3.3d
1132 -jl03 = 1137\ 5.2°
799-J138 = .814 \ 9.8°
948-j'123= 956\ 7.4°
16
TH
NN
NL
B-175
B-135
.0868 +y .1004
.0156 +j .908
.0158+j .795
. 01644 +J.01902
. 00295 +j. 1720
.00299+ j.l 506
243-j"208= 320\40.6°
2238 - y 30 - 2238 \ 0.8°
1951 -y 31 - 1951 \ 0.9°
B-88
D-175
H-175
H-135
.0203+j .641
.0168+j .765
.0178 +j .6503
.0188 +j .5687
. 00384 +y. 121 4
. 00318 +j. 1449
.00337 + j.l 232
.00356+ j.l 077
1564 -j 44= 1565 \ 1.6°
1824 -j 64= 1825\ 2.0°
1648 -y 41 = I649rT45
1419 -y 42= 1420 VI. 7°
H-88
H-44
M-88
.0238+y .4577
.0307+j .3249
.0271 +j .3773
.00451 +j. 08669
.00581 +/.Q6I53
.00513 +J.07146
1129 -j 55 = 1130 \ 2.8°
791 -y 72=* 794 \ 5.2°
934 -j 75= 937 \ 4.6°
* Mid-section iterative impedance in case of loaded facilities.
FIG. 29.
Secondary Constants of Exchange Area Cable Facilities at 1000 Cycles per Second — 22,
and 16 Gage
17-96
TELEPHONY
Exchange cables are usually of the non-quadded, paper- or pulp-insulated types, having
attenuation? losses at 1000 cycles, as shown in Fig. 26. These cables are not generally
loaded for subscriber loop use, but are frequently loaded when employed for interoffice
trunks, particularly in the larger exchange areas. The primary distributed constants of
exchange area cable facilities and of miscellaneous paired conductors for exchange use are
shown in Fig. 27. The resistances, inductances and capacitances are in d-c values, but
for practical purposes, may be considered equivalent to the 1000-cycle values. The
leakage conductances are specifically 1000-cycle values. The secondary constants of
of exchange area cable facilities at 1000
cycles, are shown in Figs. 28 and 29.
OPEN- WIRE FACILITIES for exchange
use are principally of iron or high-tensile-
strength steel, the steel being used almost
exclusively in recent years, owing principally
to economy and better service performance.
New types of steel have been developed for
telephone wire as the result of extensive
studies of the materials used, and by means
of heat and other treatments applied during
manufacture. Some buried wire (such as
W.E. Co. U or UA types, loaded or non-
loaded) is used in rural areas for short dis-
tances, the characteristics of which are given
in Fig. 27.
The a-c resistance of BB grade iron wire
and of Crapo HTL-85 and HTL-135 high-
tensile telephone line wire, over a frequency
range of 500 to 2000 cycles, using current of
CC I!
s
S
S*
oc
500 750 1000 1250 15 OO 1750 2000
FREQUENCY IN CYCLES PER SECOND
Fia. 30. Comparison of A-c Resistance of BB
tto^Ll^tl^l^l^WoS? J"^? magnitude, i. shown in Fig. 30.
1945 by Indiana Steel and Wire Co.) The smaller variation in a-c resistance of the
Crapo wire (manufactured by Indiana Steel
and Wire Co.), as compared to the BB wire, tends to reduce modulation effects on voice
currents traveling over the wire, and thus to improve the quality of the transmitted
speech. Figure 31 shows comparative breaking strengths between the above three wires,
as presented by Indiana Steel and Wire Co. Figure 32 shows the characteristics at 68
deg fahr of 109 (No. 12 BWG) high-strength steel and 134 (No. 10 BWG) steel wire with
0.8-oz zinc coating, 12-in. spacing, and DP insulators.
Copper steel wire (104 mil diameter), the characteristics of which are shown in Table
5, has roughly one-half the attenuation per mile at 1000 cycles of 109 high-strength steel
wire (Fig. 32). Thus, this wire may be used advantageously in place of high-strength
steel wire where the lower loss is required to meet exchange transmission standards. Cop-
per steel wire (0.081 mil diameter and 40 per cent conductivity) having per pair mile an
attenuation loss of 0.22 db (wet) and resist-
ance of 42.8 ohms at 68 deg fahr may also
be used where applicable.
Buried wire (paired, insulated, such as
W.E. Co. U or UA type) is sometimes used,
loaded or non-loaded, in place of or as an ex-
tension of open-wire rural plant, depending
on economies.
CARRIER CHANNELS superimposed on
rural power lines are now under trial opera-
tion to determine the practicability and re-
quirements for thus serving rural subscribers
in locations not at present served by tele-
HTL
85
BB
> 200 400 600 800 1000 1200
BREAKING STRENGTH IN POUNDS
31. Comparative Breaking Strength of BB
Grade Iron Wire and Two Types of High Tensile
Telephone Line Wire — No. 12 BWG (Copyright
by Indiana Steel and Wire Co.)
phone lines. The equipment, developed by the Bell System and designated as the M-l
carrier telephone system, is being made in quantities by the Western Electric Co., the
privilege of producing it being extended to other manufacturers.
The first two systems, installed in 1945 for trial at Jonesboro, Axk., and Selma, Ala.,
provide rural service to four subscribers over an 11-mile section of 7200-volt, multi-
grounded neutral, single-phase power line out of Jonesboro, and to four subscribers over
a 14-mile section of 6900-volt, multigrounded neutral, single-phase power line out of
Selma,
The principal elements of the rural power line carrier system, as now developed, are
shown in Fig. 33. Single channel operation is employed, using for the trials frequencies
PLANT DESIGN — EXCHANGE
17-97
0.8-oz. Zinc Coating, 12-in. Spacing, 68 Deg Fahr
DP Insulators
109 Side Circuits
Fre-
quency,
ko
Attenuation,
db/mi
Phase Shift,
radians/mi
Characteristic Impedance
Dry
Wet
Dry
Wet
Dry
Wet
0.3
1.0
2.0
3.0
4.0
.181
.289
.407
.528
.623
.207
.313
.436
.560
.660
.028
.067
.121
.167
.212
.026
.068
.095
.169
.215
1754 - yi314 = 21 92 \ 36. 83°
1279 -y 629 = 1425 \26.1 8°
1142 -y 443 = 1 225 \ 21.20°
1054 - j 383 = 1121 \ 19.97°
1004 - j 339 = 1060 \ 18.65°
1818-^1122 = 2I36\31.68°
1274 - j 578 = 1 399 \ 24. 40°
1130 -y 413 * 1203 \20.0L6
1042 -j 360 » 1102\ 19.07°
991 -y 320 = 104I\ 17.90°
109 Phantoms (of Non-pole Pairs)
0.3
1.0
2.0
3.0
4.0
.166
.259
.366
.466
.548
.195
.286
.396
.502
.588
.026
.064
.115
.160
.204
.025
.065
.116
.162
.207
969 - y 713 » 1 203 \ 36. 35°
721 -y 334= 795 \ 24. 85°
642 -y 237= 684 \ 20. 27°
598 - y 200 = 631 \ 18.50°
572 -j 176= 598\ 17.10°
1006 -y 588 = 1 165 \ 30. 30°
717 -j 300 = 777\22.70°
635 -j 215 - 670 \ 18.70°
589 -y 185 = 617\ 17.43°
563 -j 164 = 586 \ 1 6. 23°
184 Side Circuits
0.3
1.0
2.0
3.0
4.0
.136
.250
.389
.502
.599
.159
.273
.416
.533
.632
.026
.069
.120
.167
.209
.025
.070
.121
.168
.212
1563 - y 945 = 1826 \ 31. 17°
1252 - j 520 = 1356\22.55°
1084 -y 404 = 1157\20.43°
1004 - j 348 = 1063\19.12°
945 -j 311 = 995 \ 18.22°
1599 -y 788 = 1 783 \ 26. 23°
1245 -y 473 = 1 332 \ 20. 80°
1073 -y 377 = 1137X19.36°
992 - j 328 = 1045\ 18.30°
933 -j 294 = 978 \ 17. 48°
134 Phantom Circuits (of Non-pole Pairs)
0.3
1.0
2.0
3.0
4.0
.123
.220
.341
.436
.516
.149
.246
.371
.470
.554
.024
.064
.112
.156
.197
.023
.064
.114
.158
.200
883 -y 524 = 1 027 \ 30. 68°
711 -j 281 = 765 \ 21. 57°
625 -y 219 = 662\19.32°
579 -y 185 = 608 \ 17. 72°
548 -y 165= 572 \ 16. 75°
902 -y 415 « 993 \ 24. 70°
706 -j 249 = 749 \ 19. 43°
617 -y 199 = 648 \ 17.88°
570 -j 172* 595 \ 16.79°
539 -y 153 = 560 \ 15.85°
FIG. 32. Characteristics of 109 (No. 12 BWG) High-strength Steel and 134 (No. 10 BWG) Steel Wire
COUPLING POWER -DISTRIBUTION
CAPACITOR TRANSFORMER
FUIE / POWER PHASE WIRE (70OO VOLTS) { _ f/SE
ISOLATING^
CHOKE "H^
JJ^AJi^
-J H POWER NEUTRAL WIRE
^V (GROUNDED)
r°n '
JS TO
=r) OTHER
yV STATIONS
TRUNKS
OR TOLL..
CIRCUITS
TELEPHONE
CARRIER DROP
*/^WtRING INSTALLED BY
/*•' POWER LINEMAN
1<-LINE COUPLING UNIT
J (CONTAINING DRAINAGE
j INDUCTANCE FILTER AND
p
J;
<-•
-
^ *
' COUPLING
CAPACITOR
LINE
— COUPLING
UNIT
* — POLE
GROUND WIRE
TELEPHONE
— CARRIER
DROP
USUAL
— STATION
PROTECTION
INSIDE
WIRING
1
120
VOLT
— 60
— CYCLE
POWER
SUPPLY
PROTECTOR)
POWER METER— *T
HOUSE LIGHTS
AND APPLIANCES
60 CYCLE
POWER FOR CARRIER >
STATION SET
COMMON
CARRIER
TERMINAL
SERVING
UP TO 8
PARTIES',
POLE OR
OFFICE
MOUNTED
VOICE-
D-FREQUENCY
CIRCUIT
TELEPHONE ^B^
SET tea
j
USUAL VOICE
FREQUENCY
SWITCHING
EQUIPMENT
AT
CENTRAL
OFFICE
POLE->
GROUND
WIRE
SUBSCRIBER {
CARRIER TERMINAL i
,_ 1
GRC
JUNID RURAL RESIDENCE GROUND
FIG. 33. Principal Elements of Rural Power Line Carrier Telephone System (Courtesy Bell System)
17-98
TELEPHONY
of 165 kc central office calling subscriber and subscriber receiving, 195 kc subscriber call-
ing central office and subscriber talking out through central office, and 185 kc one sub-
scriber calling another subscriber on the same line but through the central-office carrier
terminal equipment. The M-l system is designed, however, for double sideband carrier
transmitted amplitude modulation, with as many as six channels, each serving eight sub-
scribers and each using three frequencies. These frequencies are different within each
channel and for each channel, being selected for transmission from the common terminal
to the stations within the range 155 to 230 kc and for transmission from the stations to
the common terminal within the range 290 to 450 kc.
Figures 34 and 35 show block diagrams of the common carrier terminal at the central-
office end of the system and of the subscriber carrier terminal (station set) , respectively,
of the types used in the trial tests.
RECEIVING
AMPLIFIER
2
—
195-KC
FILTER
FIG. 34. Block Diagram of Common Carrier Terminal at the Central-office End of a Rural Power Line
Carrier Telephone System (Courtesy Bell System)
The carrier terminals are connected to the power line through a 0.002-juf capacitor
(8700-volt rating for the trials), and a line coupling unit. This unit has a drainage in-
ductance coil, filter, and protector. All branches of the power network not used for car-
rier transmission have inserted in the primary phase conductor an isolating choke for the
main power circuit and a tap choke for branches from the main circuit. Transmission
chokes are used in branches from the main power circuit, where the branch is being used
for carrier, in order to reduce the bridging loss of the branch to through transmission over
the main line. The common carrier terminal is designed to terminate the power line in
about 500 ohms impedance for the carrier frequencies used, as are the coupling capacitors
and line coupling units at subscriber stations or at the. end of a power line tap where no
subscriber station exists.
Each carrier terminal requires continuous 110-120 volt, 60-cycle a-c power supply, and
the unmodulated carrier power delivered to the line coupling unit from each terminal is
about 1 watt. The subscriber terminal requires about 8 watts of standby and 30 watts
of operating power.
The common carrier terminal connects to the manual switchboard or dial unit over a
regular two-wire voice frequency circuit. Divided code ringing is provided using inter-
rupted carrier current in proper time sequence, or bridged code ringing can be used if
required.
PLANT DESIGN — EXCHANGE
17-99
Where the power circuit is not of the single-phase, multigrounded neutral type or it is
desired to operate more than one system on the same power line but in different sections,
special consideration of the factors involved will be required.
Preliminary data indicate that the average transmission loss between the common ter-
minal and the most distant station at the operating carrier frequencies of the M-l system,
including subscriber coupling unit bridging and transmission choke losses, will be about
2.0 to 2.5 db per mile. The overall loss between the common terminal and any station
should not exceed 35 to 40 db (15 to 18 miles of line). Under low atmospheric static con-
ditions, the carrier system can be adjusted to provide about the same effective transmission
(T •+- R)/2 from any station to the central office as would be provided from a regular
voice-frequency station having the latest-type antisidetone, local battery talking set
(W.B. Co. FIA-AST-LBT-2 cells).
The M-l carrier system may also be adapted to telephone wire lines, where additional
telephone circuits may thus be provided more economically than by other methods. This
usage requires further study.
RECEIVER
FIG. 35. Block Diagram of Subscriber Station Set of a Rural Power Line Carrier Telephone System
(Courtesy Bell System)
In operation, the system responds as though the connecting circuit between the central
office and subscriber were the usual wire line. On revertive calls (one subscriber calling
another on the same circuit or channel), the calling subscriber places the call to the called
subscriber in the usual manner (through the operator or equipment) and then puts his
handset on the cradle. When the ringing signal, which the calling subscriber hearsT is
stopped, indicating that the called subscriber has answered, the calling subscriber removes
his handset from the cradle and talks. The conversation is carried on through the com-
mon terminal, and operator supervision is provided if the office is of the manual type.
Radio channels for rural telephone service are under trial test, as discussed in article 8
of this section. It is expected that suitable equipment will be developed, based on these
tests, which will permit utilizing radio channels for this service on a commercial basis.
SUBSCRIBER LOOP DESIGN. The design procedure and considerations in engineer-
ing subscriber loop plant are briefly summarized (for a single cable route) as follows:
(a) Determine the most economical gage requirements for the ultimate area to be served
by the various complements of cable, considering both transmission and signaling design
limits, using the effective subscriber loop loss curves, if available.
(6) Examine the possibilities of obtaining further cable economies by reducing bridged
tap or distribution cable losses which were assumed in determining the design limits.
(c) Examine the possibilities of utilizing any existing plant with the new plant being
designed, without exceeding the design limits.
(d) If the loop loss or signaling limits are exceeded in existing plant, determine the
most economical plan of meeting the limits, such as using special sets, reducing bridged
cable losses, loading the longer cable pairs, or choosing larger-gage cable or long line
circuits.
17-100 TELEPHONY
(e) If some margin of loop loss and loop resistance results from the use of existing plant
in connection with the plant being designed, study the advisability of smaller-gage pairs
than indicated under (a) above, taking into consideration the permanence of the existing
facilities and the relation of the proposed plant to the ultimate plan.
(/) Combinations of gages are frequently practicable, particularly since the trend is
toward the finer-gage cable adjacent to the central office.
(g) Composite (more than one gage) cables are installed extensively, the larger gages
serving the outlying areas.
(A) Loading on long loops is sometimes employed to meet loop loss limits. H-44 or
H-88 loading on 19-, 22-, or 24-gage cable results in substantial loss reductions over non-
loaded loops, which might permit smaller-gage conductors for long loops. Bridged taps
on loaded pairs must be limited to avoid serious impairments.
(i) Signaling limits may economically be extended, in some cases by modifications or
readjustments of central-office equipment, larger-gage conductors or long line units for
the longer loops, or occasionally the use of two pairs in parallel may be justified to reduce
loop resistance.
0') Loop and trunk plant design is based on the most efficient types of subscriber sets
available or, in some cases, anticipated within a relatively short period of time.
(fc) Special exchange lines, such as private or PBX tie and foreign exchange lines, con-
ference and bridging arrangements, and one-way speech networks, require special design
work to meet their particular needs.
The zoning of subscriber sets is a procedure that provides for the introduction of station
apparatus in such a way as to obtain the desired grade of transmission at the lowest prac-
ticable overall cost. Owing to the different efficiencies of the various types of station ap-
paratus in service and under continuous development, it is necessary to insure that this
apparatus will be installed as required, so that (1) the cost of the outside plant will be the
minimum, (2) transmission will be satisfactory for the outside plant design, and (3) station
apparatus costs will be minimized by obtaining a reasonable service life for the older ap-
paratus, avoiding as far as possible premature replacements of existing apparatus and
providing an orderly program for the introduction of new station apparatus. Thus, ex-
change areas, as required, are divided into zones within which only certain types of station
apparatus may be used.
TRUNK PLANT DESIGN is based on the transmission loss limit assigned to each group
of trunks, as determined from the loop and trunk study. The design limit is obtained by
deducting from the overall permissible trunk loss (1) terminal junction losses, due to char-
acteristics of the proposed trunks, which differ from the reference trunk; (2) intermediate
junction losses, due to a trunk being composed of different types of facilities; (3) losses
due to loading irregularities; and (4) equipment and office losses at intermediate points
between the trunk terminals. Data have been prepared for the Bell System showing
both terminal and intermediate junction losses under the usual conditions encountered
in practice. In some cases, under certain conditions, these losses are actually negative
(transmission gains).
The design limits for the trunks, having been determined for the various conditions
under which the given group of trunks will operate, represent the permissible effective
trunk losses. The type of trunk is then selected which meets the design limits and has
least outside plant costs, taking into consideration existing trunk plant, future trunk fa-
cility needs over the route involved, and any other factors that may have a bearing on the
selection of the type of trunk. Figure 36 shows effective losses for non-quadded exchange
area cable trunks.
The signaling limits for trunks are based on signaling, pulsing, and supervision require-
ments, which vary materially for different types of offices and associated terminal equip-
ment. These limits, as well as leakage requirements, are usually indicated on the stand-
ard drawings for each type of central-office circuit, which may be different for the two ends
of the given trunk. The lower value, if there is a difference, will be controlling in deter-
mining the signaling limit.
Overall trunk resistance for signaling purposes is usually computed from unit values
for temperatures of 68 deg fahr. For underground trunk plant the resistance change with
temperature will be about 3 per cent maximum, which may usually be disregarded. For
aerial cable, the change may be as much as 10 to 12 per cent, and this variation of resist-
ance with temperature change should be considered in the signaling design limits.
With the larger-gage trunk facilities generally used in the past, the transmission design
limit usually controlled the selection of the type of trunk facilities, but with the higher
permissible interlocal trunk losses in recent years (resulting from allocation to trunks of
PROGRAM SERVICE
17-101
part of the new instrument gains) and the trend toward higher supervision limits with
current types of dial equipment, the field of use of the finer-gage cables has been extended,
so that signaling limits may be controlling in some cases.
Cable {
26
AST
24
ASM
22
BSA
19
CNB
19
DNB
16
TH
13
TJ •
Load-
ing
Spacing
ft
Decibels per Mile at 68 Beg Fahr
NL
3.20
2.57
2.15
1.51
1,34
0.91
0.60
M-88
M-135
M-175
9000
9000
9000
1.35
1.22
0.95
0.79
0,51
0.42
0.46
0.37
0.34
.26
.21
.17
.16
.12
H-44
H-88
H-135
H-175
6000
6000
6000
6000
1.48
1.15
1.05
0.80
0.64
0.57
0.43
0.35
0.32
0.51
0.39
0.31
0.28
.27
.21
.17
.16
.11
D-175
4500
0.52
0.29
0.26
.15
B-88
B-135
B-175
3000
3000
3000
0.87
0.61
0.49
0.35
0.27
0.26
0.31
0.25
0.23
.18
.14
.14
Decibels per Mile at 110 Deg Fahr
NL
3.33
2.68
2.24
1.57
1.39
0.94
0.63
M-88
M-135
M-175
9000
9000
9000
1.47
1.33
1.03
0.86
0.56
0.46
0.50
0.40
0.37
.28
.23
.18
.17
.13
H-44
H-88
H-135
H-175
6000
6000
6000
6000
1.61
1.25
1.15
0.87
0.70
0.62
0.47
0.38
0.35
0.55
0.42
0.34
0.31
.30
.22
.19
.18
.12
D-175
4500
0.56
0.31
0.28
.17
B-88
B-135
B-175
3000
3000
3000
0.94
0.66
0.53
0.38
0.30
0.28
0.33
0.27
0.25
.20
.15
.15
Nate: The resultant trunk loss should not be used closer tiian to nearest 0.1 db.
FIG. 36. Effective Trunk Losses — Exchange Area Cable Trunks
PROGRAM SERVICE
18. PROGRAM SERVICE
In general, program service, as furnished by the telephone companies, consists mainly
of providing suitable wire or carrier facilities to the broadcasting companies for the trans-
mission of program material, which usually originates in broadcasting studios or other
locations and which is broadcast from radio transmitters to the public.
Programs, being of a varied nature, from the finest orchestral music to ordinary speech,
require different grades of telephone facilities to meet the broadcaster's requirements. For
this reason the telephone companies have developed and have made available for broad-
casting purposes several rather broad classifications of facilities, as shown in Table 1.
SERVICE REQUIREMENTS, being more exacting for high-quality than the lower-
quality program circuits, involve the control of (1) transmission levels and losses, (2)
frequency, delay, and phase distortion, and (3) noise and crosstalk. See Section 12 for
critical cutoff points in the frequency ranges of various musical instruments and speech.
Transmission levels and losses in open wire and cable are maintained as specified, by
special program amplifiers, the latest types having a flat gain characteristic with a max-
imum gain of about 30 to 40 db and outputs of about 10 to 20 db above reference volume,
17-102
TELEPHONY
PROGBAM SERVICE
17-103
depending on the type of amplifier. The levels must be high enough to provide a satis-
factory signal-to-noise ratio and must also be coordinated with the levels of adjacent cir-
cuits or systems, to avoid causing interference in them. A variable attenuator, having a
range of 0 to 32 dfy controls the amplifier gain. Figure 1 shows a typical layout and
level diagram for a wide-band (8000 cycles) open-wire program system.
Attenuation variations in the line over the frequency band (frequency distortion) are
compensated for by low- and high-frequency equalizers of the constant-resistance type,
which correct for variations in the preceding line section, to meet requirements.
A repeating coil (impedance ratio, line to drop, of 1 : 1.15) is provided at each repeater
point between the incoming line and line equalizing apparatus, which latter is on the line
side of the line amplifier. This coil gives the proper termination to the line and insulates
the line from the terminal equipment against noise and for protection. Suitable repeating
coils are also provided at both
ends of the local loops for similar Table 1
reasons. A non-loaded cable
equalizer is provided for the local
cable loops.
Special filters are required for
facilities which transmit both
program and carrier frequencies,
in order to separate the two fre-
quency bands at the line termina-
tions and direct them into then-
proper equipments. Line filters,
designed for 5000-cycle program
systems, introduce slight delay
distortion in the program fre-
quency bands. If the number of
line sections in tandem equipped
with these filters is about eight
or more, a delay equalizer for each
two filters is necessary to main-
tain the time of propagation of
all frequencies in the program
band within satisfactory limits
(not to exceed about 0.3 milli-
second difference between maxi-
Classification of Facility
Approximate
Frequency
Band in Cycles
Intercity Circuits
1. High quality. ..
noo- 5,000
2. Medium quality
I 50- 8,000
200- 3,500
3 Speech, only . .
300- 2 500
Metropolitan Area Circuits
1. Studio-transmitter circuits for AM
stations
50- 8 000 *
2. Studio-transmitter circuits for PM
stations
50-15,000
3. Network loops — between studio and
point of connection (toll office) with
intercity network chanr^1!??
f
4. Piek-up circuits — between points of
program origin and studio or point of
connection with intercity channels . . .
t
* Band may be extended to higher frequencies if specifically
requested by the customer.
t Equalized at request of the customer for band width desired
(usually 50-8,000 cycles).
mum and minimum delays for a range of 500 to 5000 cycles). An auxiliary low-pass
filter may be provided, if required, for 5000-cycle systems, to effect further discrimination
against high-frequency interference from the line.
An auxiliary low-pass filter may be used on 8000-cycle program circuits to supplement
the low-pass filter of the carrier line filter set where further discrimination is needed.
Noise must be limited in all program circuits, so that it will not interfere appreciably
with the quality of the broadcast.
Pre distorting and restoring networks are employed in open-wire program systems,
particularly the 8000-cycle system, to minimize high-frequency noise from nearby carrier
systems. Predistortion is accomplished by introducing, at the sending end of the cir-
cuit, a network which effectively raises in volume the currents above 1000 cycles to a
higher level than normal for line transmission, thus increasing the signal-to-noise ratio at
these frequencies. Since the power at the higher frequencies is relatively small, the
amplifiers are not overloaded by this procedure. The restoring network at the receiving
end of the circuit restores the predistorted currents to their original amplitude and phase
relation. The net reduction in high-frequency interference is equal to the relative losses
introduced by the restoring network at the frequencies restored. Figure 2 shows the char-
acteristics of these networks, which are of the lattice type and are composed of combina-
tions of inductance, capacitance, and resistance elements.
Crosstalk also must be controlled. Methods of limiting crosstalk include such items as
proper selection of facilities, maintenance of proper levels, and avoidance of the adverse
effects of circuit irregularities which may develop from time to time.
PROGRAM FACILITIES may be of open wire or cable, assigned for program use^in
the program frequency band, or such facilities may consist of single-sideband transmission
over cable carrier systems, using three channels of a twelve-channel unit, or over other
carrier system channels.
Open-wire facilities for long-haul broadcasting usually consist of 165-mil hard-drawn
copper-wire circuits, although 128- or 104-mil wire is frequently used, where available and
17-104
TELEPHONY
appropriate, but generally for the shorter-haul circuits. Preference is given to 8-in. non-
phantomed pairs.
Amplifiers are spaced about twice as frequently (50 to 150 miles) for 104 circuits as for
165 circuits. Open wire, being more subject to noise and crosstalk than cable or carrier,
must be carefully selected and maintained in order to provide facilities of suitable
quality.
Cable pairs (non-quadded) may be employed for long-haul program service. The latest
type of cable system for this purpose is the 16-gage B-22 loaded system, which is satis-
factory for a band of 35 to 8000 cycles.
The 16-gage B-22 system operates over one-way transmission paths. The non-quadded
cable pairs are loaded at a 3000-ft nominal spacing with 22-millihenry coils. The attenu-
ation-frequency characteristics of this facility are shown in Fig. 19, article 16, and the
impedance, cutoff, and velocity values are shown in Fig. 18, article 16. Amplifiers and
ia
10
14
12
8
6
4
2
0
_J_J
IEDISTORTEF
TORER IN 7
J
AND
ANDE
""•—•>».
.,^
"HI-
RES
M
s
^
X
\
'""-
"^.^
/
^
X
X
/
N-
^
/
^X
'x
\
RESTORER
/
X
x
^PREDISTORTER
,^
^
X
X
xx
s
• ••
— — -
,— — • -
"
^~
"''
01 2345678
FREQUENCY IN KILOCYCLES PER SECOND
FIG. 2. Loss-frequency Characteristics of Predistorting and Restoring Networks — Open-wire Program
System (Courtesy Bell System)
associated apparatus are located at about 50-mile intervals. Attenuation and delay
equalizers, as required, are associated with each line amplifier input circuit. A supple-
mentary adjustable equalizer is usually required in each repeater regulator section, be-
cause of the variations in capacitance and conductance of the different cable sections
through which the program circuit passes. The application of this system for new instal-
lations may be limited somewhat in the future by the newer developments in single-
sideband carrier program transmission.
High-quality program circuits may be operated over cable carrier systems, using single-
sideband transmission and three channels of the system. The single-sideband system is
designed to operate over as many as ten carrier links in tandem. Figure 3 shows a sche-
matic of a single-sideband program terminal arranged for transmitting over cable carrier.
Medium-quality program circuits may be assigned to 19- or 16-gage H-44 or B-88 cable
side circuits, but non-linear and delay distortion in the repeaters and loaded pairs and
transmission variations, particularly at high and low frequencies, limit the length of these
facilities to about 300 miles for H-44 and B-88 loaded facilities. Channels of the cable
carrier system may be used for medium-quality service if not more than one link of these
carrier systems is used. Non-loaded cable is limited to relatively short lengths.
METROPOLITAN-AREA PROGRAM FACILITIES, as indicated in Table 1, are
designed to provide (1) studio to transmitter circuits for both a-m (amplitude-modulation)
and f-m (frequency-modulation) broadcasting stations, (2) network loops between the
studio and the point of connection (usually the telephone company toll office) with inter-
city network channels, and (3) pick-up circuits between the point of program origin and
the studio or the point of connection with intercity network channels.
The types of line facilities used may consist of non-loaded exchange or toll cable pairs
of various available gages, loaded exchange or toll cable pairs (where loading is required
for transmission reasons), or open-wire pairs. Metropolitan-area program circuits, to a
PEOGEAM SERVICE
17-105
large extent, employ non-loaded exchange cable pairs,
pairs, with or without intermediate ampli-
fiers.
Equalization may or may not be required,
depending on the band width to be trans-
mitted, length and gage of facilities involved,
and the transmission deviation permissible
over the frequency band.
For studio to transmitter circuits, serving
a-m stations, a relatively flat transmission-
frequency characteristic may be obtained
between 50 and 8000 cycles, using standard
equalizer equipment, for sections of non-loaded
cable not exceeding about 21.5 miles of 16-,
10.0 miles of 19-, 6.5 miles of 22-, 5.0 miles of
24-, or 4.2 miles of 26-gage cable conductors.
Longer lengths of cable may be divided into
sections not exceeding the above lengths, which
are then treated individually. It is desirable,
from a transmission stand-point, to employ a
uniform type of facility for program circuits
when available.
For studio to transmitter circuits, serving
f-m stations, standard equalizer arrangements
provide a satisfactory transmission character-
istic over metropolitan-area circuit lengths
usually encountered. In one instance, such a
circuit, consisting of 24 miles of 19- and 22-
gage cable pair (non-loaded) , with three inter-
mediate amplifiers, was equalized to limit the
overall transmission variation to 1.9 db for a
frequency band of 30 to 15,000 cycles. Wider
bands, extending to 18 or 20 kc, have been
provided in special cases when requested by
the customer, using special equalizing methods.
Carrier loaded (C 4.1 or C 4.8 loading)
cable facilities when available may be equal-
ized for metropolitan-area circuits, serving
either a-m or f-m stations. The B 22 facilities
are suitable for frequencies up to 8000 cycles
for any length of circuit likely to be encoun-
tered, using amplifiers and equalization as re-
quired.
SPECIAL FEATURES developed for pro-
gram systems include:
(a) Bridging arrangements, in which pro-
vision is made for connecting one or more
branch program circuits to the main program
circuit at a given point.
(6) Monitoring, in which attendants may
listen in and supervise programs (to insure
satisfactory operation) at designated points on
the broadcast network.
(c) Reversals, in which provision is made
for two-way transmission over the same net-
work facilities, by reversing the direction of
transmission of all connected one-way ap-
paratus at will, either manually or automati-
cally, and under control of the telephone com-
pany or the customer.
(£) Order wire and talking arrangements,
which permit the various control points and
attendants to converse readily regarding net-
work operations without interfering with the
broadcast facilities.
and in some cases open-wire
17-106
TELEPHONY
SUBSCRIBER STATIONS
19. SUBSTATION EQUIPMENT
SUBSCRIBER STATION EQUIPMENT consists of a large number of types and designs
of subscriber telephone sets and auxiliary apparatus, essential to the furnishing of a com-
plete telephone service in the most economical and satisfactory manner.
The basic subscriber telephone set is assembled in a number of designs to meet the
needs of different services and the subscriber's convenience, but the operating principle is
primarily the same for all these sets. The
basic set consists principally of a trans-
mitter, receiver, induction coil, condens-
ers, ringer, and spring assembly (switch-
hook), suitably mounted in a metal or
plastic housing. The set will also have
a dial if it is connected to a dial exchange
or unit, and for magneto telephones a
dry-cell battery for transmitter current
and a magneto generator for signaling
must be provided.
THE TELEPHONE TRANSMITTER
is designed to receive airborne sound
waves of various frequencies and convert
them into electrical waves of similar fre-
quencies for transmittal over a telephone
circuit. It is essentially a device which
makes it possible for relatively weak
sound energy to control electrical energy
of greater average strength.
The modern transmitter unit employs
an insulated, spherical-shaped carbon
chamber holding the carbon granules, and
a very light metal conical diaphragm, with
a dome-shaped center, which is positioned
in the carbon chamber in such a way as
to hold the granules in the chamber. The
dome and chamber are the front and
back electrodes, respectively, of the unit.
Figure 1 shows a cross-sectional view of
the Western Electric Co. No. Fl unit.
The electrode surface area in contact with the carbon granules is the same, regardless of
the position in which the transmitter is used. The No. Fl unit has a resistance (new)
of about 30 to 40 ohms and is applicable to any type of subscriber telephone set of
Western Electric Co. make. Transmitter current should not exceed about 100 milliam-
peres for normal usage and life. A small condenser is usually connected directly across
PAPER BOOKS ~
DIAPHRAGM
SILK CLOSURE AND
CONTACT MEMBER'
MOVINS-FRONT
ELECTRODE '
ATTACHED TO
DIAPHRAGM
OILED-SILK
MEMBRANE
DIAPHRAGM
BRASS GRID
— INSULATORS
FIG. 1. Cross-sectional View of Modern Non-posi-
tional Transmitter Unit (Courtesy Bell System)
—30
A
• -»v.
-40
Kl
X(
X
sJil^,
S"
^
— r
/
V v*-
395 '
s /
X<\
\
^^
"^^
n
/-''
337
V
O O5 1.0 1.5 2.0 2.5 3.0 3.5 4.O 4.5 5.O
FREQUENCY IN KILOCYCLES PER SECOND
FIG. 2. Transmitter Response Characteristics (Courtesy Bell System)
the transmitter electrodes of the Fl.unit, when used in handsets, to minimize packing
(welding together) of carbon granules as the result of arcing in the carbon chamber when
the transmitter current is rapidly interrupted by switchhook flashing or other operations.
SUBSTATION EQUIPMENT
17-107
AIR CHAMBER
WJNDJIvKS
PERMALLOY
POLE FHECE
The response of all makes of the modern non-positional transmitter is greatly improved
°TT^e™T%S2eS' as ^own for Western Electric Co. instruments in Fig. 2.
IMJi, l&iJiPHONE RECEIVER is designed to receive electrical waves of various fre-
quencies and convert them into sound waves of similar frequencies for the listener's ear.
It is essentially a reconverter from electric to sound energy (within its frequency range)
and is a necessary complement of the transmitter in the transmission of speech.
The modern receiver is generally of the unit or capsule design, which is applicable to
various types of telephone receivers and
assembled sets as made by the respec- ifl^Kfffr .xREMAUjor BAR MAGNET
tive manufacturers. One make (W.E.
Co. HA1) consists principally of a bipolar
permanent magnet, with the parts as-
sembled in a zinc alloy frame. The
diaphragm of Permendur is seated on a
ring projection of the frame, just above
the magnet, with an air chamber of def-
inite volume behind it. This chamber
has a small outlet hole covered with a
silk disk of specified acoustic impedance.
The diaphragm also has an air chamber
of definite volume between it and the
receiver cap, which latter has six holes
of definite length and area. The un-
clamped diaphragm thus rests between
two air chambers of specified volumes
and outlet impedances, and variations
in receiver efficiency with temperature
changes as well as diaphragm freezing to
the pole pieces are practically eliminated.
The HA1 receiver unit has a working
impedance at 1000 cycles of about 140
ohms with a positive angle of 60°. Figure 3 shows a cross-sectional view of this type of
receiver unit, and Fig. 4 shows its response characteristic as well as that of the older type
W.E. Co. No. 557 receiver.
The HA1 receiver is affected adversely by d-c flow of either polarity, which for 100
milliamperes amounts to about 4.5 and 6.0 db loss in volume efficiency for the opposing and
aiding directions, respectively, of current flow.
The anti-sidetone type induction coil is now generally employed, in place of the older
sidetone type. Figure 5 shows schematic diagrams of both sidetone and anti-sidetone
station circuits and the
direction of instantane-
ous current flow for both
the transmitting and re-
ceiving conditions-
In the sidetone connec-
tion (Fig. 5, circuit 1),
the speech currents pro-
duced in the transmitter
divide between the A and
B windings (solid arrows) .
The current in each of
these windings induces a
voltage in the other wind-
ing (dashed arrows) .
The two currents in A
combine to flow out over
the line, and the two
currents in B combine to
flow through the receiver
ZIlsJC ALLOY FRAME
PIG. 3. Cross-sectional View of Modern Receiver Unit
(Courtesy Bell System)
RESPONSE IN DECIBELS
(0 DECIBELS = 1 BAR PER WATT)
& 8 8 3 § 2
/
\
CLOSED- COUPLER RESPONSE
(CLOSED -COUPLER VOLUME = e cc)
—•
^
\
\
"^
RECE
EMPLOY
HA1
-* —
\
IVER
NGTHE
x\
1 /
' i r
\
\
557
TYPE RECEIVER
*^S
1 'V
\
i!
O OS 1.O t5 2.0 2^ 3.0 3^ 4Q
FREQUENCY IN KILOCYCLES PER SECOND
PIG. 4.' Receiver Response Characteristics (Courtesy Bell System)
and produce sidetone. When receiving, the incoming current divides between the trans-
mitter (T) and the receiver C5) branches (solid arrows). The current in A induces a
voltage in B, which establishes an opposing current in B (dashed arrow), but the incom-
ing line current in B is larger, so that the resultant current through R is sufficient to
actuate the receiver diaphragm.
The sidetone reduction connection of the sidetone coil employed on short loops having
17-108
TELEPHONY
the sidetone type of subscriber set is shown in Fig. 5, circuit 2. With this connection the
transmitter current cannot flow directly through the receiver (R) branch, but some in-
duced current does flow through R because of the inductive coupling between windings A
and B, Since transmitter current does not flow directly through B, this winding does not
induce a voltage in A, such as occurred in the sidetone connection, and the transmitter
line current is not thus aided, resulting in lower transmitting efficiency. In receiving,
the incoming line current does not enter the B winding directly but flows through winding
A, establishing an induced voltage from A to 5, which causes received current to flow
through R. Thus, the induced R current is not opposed by line current flowing directly,
as was the case in the sidetone connection, resulting in slightly higher receiving efficiency.
SIDETONE CIRCUITS
-STANDARD CONNECTION
SIDETONE REDUCTION
CONNECTION
RECEIVING (CIRCUIT 3)
TRANSMITTING (CIRCUIT 3)
CIRCUIT 3
FIG. 5. Sidetone and Anti-sidetone Station Circuits (Courtesy Bell System)
In the anti-sidetone connection (Fig. 5, circuit 3), a third winding of relatively high re-
sistance, so that the winding has both an inductance (C) and resistance (N) component,
has been added to the sidetone circuit.
In receiving, the incoming current divides between the transmitter (T) branch and
winding B (solid arrows). The current in B divides between the receiver (R} branch
and the winding C (solid arrows). The currents in A and B induce voltages in C, and,
by properly proportioning the coil winding relations, the current in C (dashed arrow)
resulting from these combined induced voltages is opposite and about equal to the current
flowing directly in C. The C winding thus has no appreciable effect on receiving volume,
and the receiving efficiency of both the sidetone and anti-sidetone circuits is about the
same. However, owing to sidetone suppression, the effective receiving losses for the anti-
sidetone circuit are substantially less.
In transmitting, the transmitter (T) output current divides between the windings A
and B, and the current entering B divides between the receiver (R) branch and the C
winding (solid arrows). These currents in A and B induce voltages in B and A, respec-
tively, resulting in an induced current flowing in an aiding direction in the line and in
B (dashed arrows) . The induced current in B divides between R and winding C (short
dashed arrow) . Also, there is induced in C a voltage (resulting from the currents flowing
in A and B directly from the transmitter) which establishes a current in C (long dashed
arrow) . The combined currents in C flow through R in a direction opposite to the current
(solid arrow) which comes directly from the transmitter. Since these opposing currents
are, by design, about equal, the receiver is not appreciably affected during transmitting,
and sidetone is practically eliminated. The transmitting volume efficiency of both the
anti-sidetone and sidetone circuits is about the same, but the effective transmitting losses
for the anti-sidetone set are substantially less, principally because, when less sidetone is
heard by the talker, he unconsciously raises his voice level until the sidetone heard is
about equal to what he is accustomed to in ordinary conversation. Increased voice level
results in transmission gain. ,
SUBSTATION EQUIPMENT 17-109
The range of line impedance conditions is usually much greater for the local battery
anti-sidetone set which is used on the longer loops into outlying and rural areas. In order
to provide an approximate balance for these line conditions, the local battery anti-side-
tone circuit is designed with a balancing network that can be connected for a line im-
pedance of 600, 900, or 1500 ohms (angle 50°).
Under average conditions, and depending upon the amount of sidetone reduction which
may be effected in any particular case and upon the circuit design, a transmission im-
provement of about 5 db may be expected from use of the anti-sidetone in place of the
sidetone circuit.
THE RINGING CIRCUIT of a common-battery subscriber set includes a ringer and
condenser, but a condenser may or may not be required in this circuit for a magneto set.
The common-battery sidetone circuit has a single condenser for use in both the receiver
and ringer circuit, but with development of the anti-sidetone circuit a separate condenser
is used hi the receiver and ringer circuits. "With the two- (split-) condenser arrangement
and high-impedance ringers, the susceptiveness of the subscriber set to incoming line noise
is materially reduced over the single-condenser set, especially on balanced party-lines (same
number and type of ringers connected to ground on each side of the line). Ringers are
manufactured in a large number of types (usually with permanent magnet yokes and bias-
ing springs) and impedances for use with the several signaling systems and to meet signal-
ing requirements. The types of signaling systems used include straight line (20 or 16 2/3
cycle), harmonic, superimposed, and pulsating ringing, of which straight line ringing is
commonly used for individual line, two-party selective, four-party semi-selective, divided
code, or non-selective bridged stations.
Harmonic ringers are designed for frequencies of 16.6, 20, 25, 30, 33.3, 42, 50, 54, 60,
66, and 66.6 cycles. These ringers have reeds of different weights which respond only to
the frequency for which they are designed. The harmonic system provides selective
signaling for up to five bridged or ten grounded ringing stations (five connected to ground
on each side of the line) .
Superimposed ringing requires the superimposing of d-c potentials (positive and nega-
tive) on the regular a-c ringing current in order to raise the peak positive and negative
voltages sufficiently to break down a three-element, cold-cathode, vacuum-tube gap,
which is connected from line to ground at each station. The tube may be so connected
that its gap will break down when either the positive or negative combined potential is
applied, but not both. The ringer is connected between one element of the tube and
ground so that, when the tube functions, the a-c ringing current will operate the ringer.
This type of ringing is used in four-party selective and eight-party semi-selective service.
The control gap of one type of tube has a nominal breakdown of 70 volts, and the nominal
main (ringing) gap sustaining voltage is 75 volts.
A-c relays, first used in this type of service, generally have been replaced by the
tube.
Pulsating ringing employs positive and negative pulsations sent out over the line from
the office. The station ringers are biased with a spring so that they operate when either
the positive or negative pulsations are applied, but not both. This type of ringing may
be used for four-party selective or eight-party semi-selective service.
Ringer impedances are designed to meet various service conditions. The low-impedance
group will have d-c resistances of from 1000 to about 2500 ohms, and the high-impedance
group of from 3500 to about 5700 ohms or more.
Usually each ringer has a biasing spring, one end of which is attached to the armature
and the other end, by means of a winding cord, to an adjusting stud on the ringer frame.
Thus, the armature can be tensioned or biased to the degree necessary for the type of
service involved, and to avoid cross rings and also bell taps during switchhook and dial
operation. Ringers may be of the polarized or non-polarized type, depending upon the
type of ringing system employed.
The number of ringing bridges across a line or from either side of a line to ground is
limited to a total capacitance of the ringer condensers not to exceed 2 /if where not more
than eight such bridges are involved on non-polarized lines.
Condensers are usually of 2-/if capacitance when used in single-condenser sets and in
the transmission circuit of two-condenser sets. The ringer circuit of these latter sets may
have a condenser of 0.5- to 1.0-^f capacitance, depending upon the ringer impedance, or
for some types of magneto stations the condenser may be omitted.
Hand generators of the three- or five-bar type, depending upon the length of line and
number of bridged stations, are generally necessary in magneto subscriber sets for signal-
ing the office or another subscriber on the same line. These generators carry a spring
assembly which functions to open and close the generator circuit across the line when the
17-110
TELEPHONY
generator is idle and operating, respectively. Figure 6 shows a view of a five-bar gen-
erator (Stromberg-Carlson make) .
The switchhook spring assembly in subscriber sets generally consists of two pairs of
make-break springs which automatically close and open the transmitter and receiver
circuits when the handset is lifted from and restored to its cradle. These springs are de-
signed to retain their adjustments over long periods of time. One manufacturer is using
heavy-gage, phosphor-bronze with precious-
metal contacts, which provide positive, non-
microphonic contact.
Dials are required at all dial stations
served by mechanical offices or private
automatic exchanges of any type. The
dial is the subscriber's only means at dial
stations of securing connection with other
dial subscribers or with toll or assistance
operators in his exchange area. Figure 7
shows front and rear views of one type of
dial assembly. The front view shows the
finger wheel and stop and the number plate
with its letter and number designations
appearing through the finger wheel holes.
The rear view shows the spring assembly,
consisting of shunt (off normal) springs
which short-circuit the transmitter and
open the Deceiver circuits during dialing
and the impulse springs which open and
close the subscriber line circuit, thus causing
pulses of current to flow in this circuit at an average rate of about 10 pulses per second.
The finger wheel, having been turned to the finger stop for any selected letter or number,
is released, and as it returns to normal under spring action it is geared to operate the pulse
pawl at a speed controlled by the governor. The pulse pawl alternately opens and per-
mits the impulse springs to close as many times as there are units in the digit pulled.
Small filters consisting of inductance, capacitance, and resistance are generally bridged
across the impulse spring contacts in order to reduce dialing interference to nearby radio
receivers.
Housings of various types are provided, in which the required subscriber telephone set
units described above are assembled. These housings are made of zinc alloy, plastics,
steel for baseplates, and other materials, including rubber for cushioning. The various
units are usually assembled on a universal baseplate, suitable for wall or desk-type sets.
berg-Carlson Co.)
Rear of Dial
Case,
ulse Contacts
'ulse Pawl
inger Stop
'Finger Wheel
Off Normal
Contacts
FIG. 7. Front and Rear View of Dial as Used with Dial Type Subscriber Telephone Set (Courtesy Bell
System)
In one type of set, made by the Kellogg Switchboard and Supply Co., plug-in type in-
duction coil (AST) and condenser units permit ready replacements to be made by pulling
out the unit to be replaced and plugging in the new unit. The design of this company's
set includes a universal permanently wired circuit, consisting of a stamped metal grid
nested in the underside of an interconnecting block which mounts on a baseplate. This
grid is connected through the block to screw terminals and pin jacks mounted on the
upper side of this block. The induction coil has a three-way and the condenser a two-way
switching unit to permit convenient circuit adjustments.
SUBSTATION EQUIPMENT
17-111
Some companies are now providing non-interfering or press-to-talk features in telephone
sets intended primarily for use on multiparty rural lines, to permit listening on the line
without the transmitter being cut into the circuit and without interfering with the ringing
and dialing or with conversations in progress.
HAND SET CORD
* IF FILTER IS NOT USED CONNECT THIS LEAD TO THE
*Y* TERMINAL OF THE DIAL
FIG. 8. Schematic of Wiring of Subscriber Hand Telephone Set — Common Battery Talking — Common
Battery Signaling (Courtesy BeU System)
Figures 8 and 9 show, respectively, schematics of the wiring of a typical common bat-
tery talking-common battery signaling (CBT-CBS) and a typical local battery talking-
common battery signaling (LBT-CBS) subscriber hand telephone set for individual, two-
party selective, or four-party semi-selective service. The dial and filter circuits are re-
quired for dial service only.
*1F FILTER IS NOT USED
CONNECT THIS LEAD TO THE
*Y* TERMINAL OF THE DIAL
FIG. 9. Schematic of Wiring of Subscriber Hand Telephone Set — Local Battery Talking — Common
Battery Signaling (Courtesy Bell System)
SUBSCRIBER SERVICES involving other than the regular subscriber telephone set
just described require a wide variety of substation apparatus. Owing to limited space in
this handbook, only brief mention can be made of some of the principal services currently
rendered, which are:
1. Station wiring plans, whereby individual central office, PBX, or private lines may
be connected at one or more telephone stations of which one or more or none may have a
17-112 TELEPHONY
regular attendant. In these cases, each station telephone may be equipped in its base
with several pushbutton type keys, or separate key boxes may be provided which can be
used for originating, answering, intercepting, holding, or transferring central-office calls
on one or more lines, or connections can be established between stations without using
either a central-office or PBX line. Various arrangements for controlling, locking out,
grouping, or extending station calls are also available. Signaling between stations is
usually by a pushbutton and buzzer circuit with battery or low voltage alternating cur-
rent derived from the commercial power supply. Operating power may be supplied lo-
cally or from the central office.
2. Loudspeaking and distant talking systems may be employed between a master and one
or more regular stations, facilitating communication, and such systems may be associated
with regular telephone facilities and equipments. These systems require amplifiers,
which are associated with each loudspeaking and distant talking telephone set, to provide
adequate volume from the loudspeaker. Commercial power is usually employed for this
equipment.
3. An operator-type transmitter and receiver set, with an associated key and jacks, may
be provided at subscriber stations to facilitate handling messages over the telephone.
4. Loudspeaker conference service may be provided, where groups of people desire to
listen to a local or distant talk and are assembled at one or more points. An amplifier
and loudspeaker with a suitable subscriber set and switching keys are required for this
service. Commercial power is used for this equipment.
5. Coin collectors of various types are located in public places where customers may
place local or long-distances calls, either by prepayment or postpayment of the charges.
Some of these collectors are placed in booths; others, in the open at locations convenient
for public use.
6. Subscriber amplifier deaf set equipment provides for amplification of the incoming
voice currents before reaching the subscriber's receiver. The incoming volume level is
raised sufficiently, in many cases of deafness, for the subscriber to carry on a telephone
conversation which would otherwise not be possible.
7. Code calling systems sound code signals at various points throughout a subscriber's
establishment to notify certain employees or officials that they are wanted at the telephone
or for some other reason. The controlling station on this system is usually located at the
subscriber's PBX switchboard and is operated by the PBX attendant as a separate sys-
tem, or the system may be actuated directly from a dial PBX or PAX system without an
attendant.
This system requires code sending and station signal equipment, properly located and
interconnected by wiring. Commercial a~c power supply is employed for operating it.
8. Loudspeaker paging systems are designed to provide a means of simultaneously
transmitting messages or announcements verbally from a central location to a number of
points within an establishment. These systems have a variety of uses from summoning
a person to a telephone or directing employee activities, to providing information to a
limited area.
9. Subscriber telephone sets for explosive atmospheres are available for use in mines, oil
refineries, or munition plants. The equipment is designed to prevent sparking of the
various parts under operation, causing explosions.
10. Outdoor-type telephone sets are provided for mounting in outdoor places for fire,
police, taxicab, and other services. These sets are enclosed in cast-iron or wooden hous-
ings, which protect the equipment from weather conditions.
11. Sound powered telephones are provided in locations where it is desired to avoid pos-
sible central energy failures and where the distances between stations are relatively short,
such as in an establishment, on a ship, or as portable field telephone equipment where
batteries are not desirable. These telephones operate through action of sound waves
striking the transmitter diaphragm and causing a variation in a magnetic field which pro-
duces electric currents in the telephone circuit of frequencies similar to those in the sound
waves. The receiving apparatus functions quite like the regular telephone receiver.
12. Program distributing systems are designed to furnish program material, either from
broadcasting stations or central program points, to hospitals, schools, hotels, business
establishments, factories, homes, and many other locations. Program material may con-
sist of music, speeches, announcements, and various other features of interest. This
material is usually transmitted over wire lines from its source to one or more common
amplifiers and thence distributed to subscribers over wire lines to loudspeakers at the
various locations.
SUBSCRIBER STATION PROTECTION 17-113
20. SUBSCRIBER STATION PROTECTION
Substation protection is required to protect subscribers and substation equipment from
dangerous voltages and currents. The telephone plant is designed to withstand, with
some margin, its normal operating currents and voltages. But there are other sources of
electrical power, chiefly lightning and commercial power linea, which may under certain
conditions impress large and destructive voltages, with resulting excessive currents, on the
telephone plant, either by direct contact or by induction.
Danger from lightning in cities is less than in sparsely settled areas because of the shield-
ing effect of buildings, trees, and various overhead structures. The danger from power-
line ^contacts with aerial telephone plant is always present where the two types of plant
are in close proximity, although material progress has been made in lessening this hazard
over the years by improved methods of construction and protection. Stations connected
to lines which are exposed to more than 250 volts between wires usually require protection
and are classed as exposed stations.
The maximum voltages most commonly impressed on subscriber lines for telephone
purposes range from 24 to 50 volts direct current and from 75 to 175 volts alternating
current. Direct-current flow over the subscriber loop (mdividual line service) does not
usually exceed 150 to 200 milliamperes and in most cases is less than about 100 milli-
amperes.
One type of substation 'protector widely used consists principally of two pairs of carbon
protector blocks (open space cutouts) and two line fuses (one pair of blocks and one fuse
for each side of the line) , with associated spring and terminal holders, mounted on a por-
celain base. Another design employs two metal plates, each of which connects with one
side of the Hne and has a sawtooth inner edge positioned 0.004 in. from a grounded carbon
block. The discharges take place across this gap. The ground electrode of the protector
must be well grounded in every case.
CARBON" PROTECTOR BLOCKS (sometimes designated as lightning arresters or
dischargers) are manufactured hi several designs, with the gap between the Hne and ground
block varying from about 0.003 to 0.075 in. or more. The dielectric between the blocks
may be air, or mica or acetate separators may be used. One design common throughout
the United States consists of a grooved porcelain block with carbon insert for the line
contact, and a solid flat (plain) carbon block for the ground contact. The Hne spring
bears against the carbon insert set in the porcelain frame, and the porcelain frame bears
against the ground block. The carbon insert is held in place by a glass cement of low
melting point, and is forced against the ground block when arcing across the gap is
sufficient to soften the cement.
The carbon insert is accurately positioned in its porcelain frame to provide a 0.003-in.
gap for substation protection, or, when used at the junction of cable and open wire lines,
this gap is 0.006 in. The peak breakdown voltages for these gaps are about 350 average
and 550 maximum for the 0.003-in. gap and about 710 average and 1080 maximum for the
0.006-in. gap.
The fuses, being connected in series with the line and on the line side of the protector
blocks, are designed to open each side of the line when the protector blocks discharge heav-
ily or break down completely and when the resulting current through the fuses exceeds
their ratings, which are usually 5 or 7 amperes, although fuses of other amperage may be
used, depending upon operating company requirements.
Grounding of the protector requires a reasonably low-resistance ground (less than about
25 ohms), which may be obtained at the subscriber's premises by connecting to (1) the
public water pipe system, (2) a private water pipe or well casing system, or (3) a driven
ground (ground rod or pipe) , preference being given in the order named.
A common ground with the secondary neutral of power distribution wiring is usually
employed at the subscriber premises unless adequate separation between the telephone
and power wiring on the premises can be maintained. This is to avoid excessive poten-
tials being impressed on the telephone wiring, where separate grounds are employed,
should there develop abnormal currents in the secondary neutral due to its becoming
crossed with the primary power circuit.
Where extensive public water pipe or other systems having a low resistance to ground
are available, common grounding should be used. Where such systems are not available,
consideration must be given, in deciding on a separate or common ground, to the prob-
ability of high potentials being impressed on the telephone wiring in case of high currents
in the secondary neutral.
Figure 10 shows one type of substation protector, widely used, with a fuse mounted
along each side and the protector blocks held in a spring assembly set in a well in the
17-114
TELEPHONY
center of the porcelain mounting block. The metal cap shown screws down over the
blocks, excluding dirt and moisture.
Substations located at power stations generally require special protection. Whenever
an abnormal condition on a power system results in ground current between the power
station and an outside point on the system, the ground-potential rise at the power station
above that of distant grounds will depend on the IZ drop in the power-station ground.
FIG. 10. Substation Protector (Courtesy BeU System)
Such a potential rise might exceed the breakdown potential of the usual telephone pro-
tector and render the telephone circuit inoperative at a time when it is most needed. Spe-
cial protective devices, consisting of a neutralizing transformer or remote grounding of the
telephone protector, may be considered in determining the type of special protection to
use.
21. PRIVATE BRANCH EXCHANGE EQUIPMENT
Private branch exchange (PBX) equipment, as discussed here, includes manual and dial,
cordless and cord, attended and unattended switchboards, whatever particular designa-
tions (such as PAX or PABX) are given to them by various companies. These boards
range in size from the small ten-line system to the largest multiple type having a capacity
of about 3000 lines or more.
MANUALLY OPERATED PBX BOARDS may be of the cordless type serving a few
stations or of the cord type for the larger installations. These boards may also be oper-
ated in conjunction with PBX dial equipment.
A typical type of manual cordless common-battery PBX board has a capacity of twelve
extensions (stations), five central-office trunks, and five connecting circuits. Each ex-
tension and each trunk terminates in a vertically mounted key unit which has three keys
with levers in a vertical row. Each key lever can be operated either up or down or remain
in its normal middle position. The upper and middle horizontal rows of keys, when op-
erated up or down, connect their respective trunks or extensions to a common strapping
between the keys in the board, and the lower horizontal row of keys does likewise when
operated to the up position. In the down position, these latter keys bridge a holding coil
across the trunk for the trunk keys and apply ringing current to the extensions for the ex-
tension keys, and the ringing keys are non-locking.
Each trunk has a visual drop and condenser bridged across it, and each extension has a
visual signal in series, so that the central office and the extensions can each signal the at-
tendant. A supervisory relay is provided in each connecting circuit, which circuit also
provides talking battery for extension to extension connections, through a retard coil.
For trunk to extension connections, talking battery is furnished over the trunk from the
central office. The attendant's telephone set is connected to the first vertical key unit on
the right side of the board.
Nominal power of 24 volts direct current is required for talking battery between ex-
tensions or between the attendant and the extensions and is usually furnished over cable
pairs from the office, as is the required 20-cycle ringing current for the board. A hand
generator is provided for the board for emergency use or where office ringing power is not
available.
Incoming rings over a trunk operate the trunk drop, and the attendant answers by
operating an idle connecting circuit key associated with the trunk, and also the attendant's
PRIVATE BRANCH EXCHANGE EQUIPMENT 17-115
corresponding key, both in the same horizontal row and to the same position, up or down.
This connects the attendant's telephone to the trunk line.
If an extension is being called over a trunk, both trunk and extension keys are operated
to corresponding positions and the extension ringing key is operated. When or before the
extension answers, the attendant restores the attendant's telephone set key to normal, and
when the supervisory signal indicates that the conversation is finished both the trunk and
extension keys are operated to normal.
Extension to extension calls are established similarly by properly operating the calling
and called extension keys.
Trunk calls can be held by the attendant operating the trunk holding key. The at-
tendant or any extension may dial through the board to a dial office, if the telephone set is
equipped with a dial. Outgoing trunk calls signal in to a manual common-battery office
automatically.
Another type of manual cord common battery PBX board has a capacity of 320 extensions,
15 central office trunks, and 15 cord circuits. This board is of the two-panel, single-
position, non-multiple type suitable for medium-size installations ranging from 80 to 320
extensions. Two boards may be operated side by side to increase the capacity. The
trunks, central office or tie (to another PBX), and the extensions terminate on jacks be-
tween which the connections are established by means of the cord circuits. The trunks
are ringdown incoming to and automatic signaling outgoing from the PBX. Each pair
of cords has a talking and listening key and a ringing key for ringing on either the front or
back cord, and double lamp supervision, except that supervision is provided on the ex-
tension cord only, for trunk calls. Each trunk and extension circuit is equipped with
lamp signals for signaling the attendant, and up to 20 line relays may be provided for ex-
tensions to increase their signaling limit.
The attendant's telephone circuit contains a dial for dialing on dial trunks or extensions.
The board may be operated in conjunction with dial PBX boards for intercepting calls
or other services.
Talking battery is supplied for extension to extension connections through the single
bridged retard coil in each cord circuit, but for trunk to extension connections talking
battery is furnished from the central office. Nominal 24-volt battery required at the PBX
for talking and circuit operations, and 20-cycle ringing power for ringing extensions, are
usually provided over cable pairs from the central office. A hand generator is usually
furnished for emergency use.
This board is designed to establish connections between local extensions and between
these extensions and a manual or dial central office or other PBX.
Incoming calls from either a trunk or extension to an extension light an associated lamp
signal at the board, and the attendant answers by operating the talking and listening key
of the answering cord, which has been inserted in the calling jack. The connection is then
completed by inserting the calling cord in the called extension jack and ringing this ex-
tension. Outgoing calls to the central office are handled over a trunk similarly, except
that signaling the central office is usually automatic.
A type of large manual cord common-battery multiple PBX board has a capacity of 1520
extensions (without designation strips), 240 trunks, and 15 cord circuits (per position).
The number of extensions may be increased by using a 34 l/2-in. in place of the usual
24 Vs in. jack panel opening. There are two panels per position and four panels per
multiple jack appearance for both extensions and trunks and one position per switchboard
section.
The trunks and extensions terminate on series cutoff type jacks in the face of the board,
and each jack has a multiple line lamp (for manual operation) associated with it. Since
each extension or trunk appears in the jack multiple at every fourth panel throughout the
board, the multiple lamps can be arranged to light, for an incoming call, at each appear-
ance up to a total of four, thus attracting the attention of a greater number of attendants
and improving answering performance. Line relays may be provided for the extensions
to increase their signaling range. The manual trunks are usually ringdown incoming and
automatic outgoing, and for a dial office they are of the dialing type.
The cord circuits are of the bridged-impedance series-condenser type, which provide
battery feed to each cord of the pair separately through bridged retard coils. The tip and
ring of the cord pair each has a condenser in series which prevents d-c flow hi one half of
the cord circuit affecting d-c flow in the other half. Talking battery is thus supplied each
extension from the PBX cord circuit for extension to extension calls and to the extension
for tie trunk to extension calls. For central-office trunk to extension calls the cord cir-
cuit is so arranged that extension talking battery is furnished from the central office, except
where PBX long line circuits are provided at the PBX.
Each cord pair has a talking and dial key and a ringing key for ringing on either the
17-116 TELEPHONY
front or back cord. Double lamp supervision is provided for each cord circuit on extension
to extension calls, and single supervision for trunk to extension calls. A position dial may
be cut in on any cord for dialing by operating the talk and dial key.
The distributing frames are enclosed in sections at the head of the switchboard. Fac-
simile sections may also be located in the switchboard line-up. The board may be oper-
ated in conjunction with dial PBX boards for intercepting or other services.
The power required for operation of this board is a nominal 48-volt d-c source for talk-
ing and circuit operations, and 20-cycle ringing current. Owing to the usually relatively
heavy battery drains, storage batteries are provided at the PBX and charged by a separate
power unit at the PBX or, where economical and practicable, over cable pairs from the
central office. Ringing current is also generally supplied to the PBX over cable pairs
from the office, and each position is equipped with a hand generator for emergency use.
This board is designed for establishments, such as large department stores, institutions,
and organizations, where PBXs of the smaller types are not adequate. It may be oper-
ated in manual or dial office areas and in conjunction with other manual or dial PBXs.
Operation is similar to a regular exchange manual switchboard except for the several
special features that may be provided to meet the individual subscriber's needs.
A typical medium-size dial PBX unit of the step-by-step (SXS) type has a capacity
of up to 79 extensions, 10 central office and 10 attendant's trunks, for two-digit dialing.
The SXS equipment consists principally of 20 line finders, 100 line and cutoff relays, and
miscellaneous equipment mounted on the side of the switch frame, and 20 selector-con-
nectors and 19 trunk equipments mounted on the reverse of the frame.
This PBX unit functions with a suitable companion manual PBX containing a jack
appearance for each trunk and extension for the purpose of receiving, originating, and
intercepting calls that cannot be handled by the SXS unit. Incoming calls reach the
manual attendant, who dials the called extension over an attendant's trunk. Outgoing
calls may be handled and calls requiring special treatment are usually handled at the man-
ual board. The SXS unit handles direct calls between extensions and from extensions to
the central office, associated manual PBX board, and other PBX boards equipped to re-
ceive dialing pulses.
Power requirements for the SXS unit consist of nominal 48 volts direct current for
talking and circuit operations, and machine ringing current. D-c power is usually sup-
plied by a small power unit located at the PBX, or over central-office cable pairs if the
load permits and pairs are available. Ringing current is generally furnished over central-
office cable pairs.
Dialed calls are completed by the usual step-by-step processes (described elsewhere in
this section) . Calls handled at the manual PBX may either be dialed in dial office areas
or completed over automatic signaling trunks in manual office areas.
Dial PBX units of the step-by-step type having capacities up to 3200 extensions, depend-
ing upon the number of extensions required, are available. Two-digit dialing (under 100
extensions) requires line finders and selector-connectors (operating as a selector on the
upper levels and a connector on the lower levels) while four-digit dialing requires first and
second selectors and connectors. If incoming dial repeating trunks are provided, they
terminate on incoming connectors for two-digit and on incoming selectors for three- or
four-digit dialing. The line finders have a 200-point bank; the other switches have 100-
point banks.
These dial PBX units are usually associated with manual PBX units, the latter receiving,
originating, and intercepting calls that the SXS unit is not arranged to handle. The SXS
unit handles calls between extensions and calls to the central office or to another PBX
which are capable of receiving dial pulses from the extensions or over dial repeating trunks.
The extensions of the SXS unit may be reached direct from other PBXs if proper dialing
facilities are provided, but calls to these extensions from the central office are usually
handled at the manual PBX board.
PROTECTION for PBX trunks and extensions at the PBX is the same as for regular
subscriber to central-office lines of the same classification, that is, exposed or non-exposed.
In addition, owing to paths to ground through the equipment in the PBX board, which
may permit foreign currents large enough to cause trouble to flow through the equipment,
heat coil type fuses having the same operating characteristics as central-office heat coils
(except that they open rather than ground the line wires) are provided in each exposed
trunk and extension at the PBX. In the case of large PBXs a section of fine-gage cable
sometimes is used in place of the 7-ampere line fuses. This is similar to the fusing pro-
vided at central offices (see article 6).
ORDER TURRETS, manufactured in various types and capacities, are employed in
business or service establishments, such as department stores, telegraph offices, taxicab
companies, and newspaper offices, to receive orders for goods or requests for services.
PRIVATE BRANCH EXCHANGE EQUIPMENT 17-117
One type of order turret for multidepartment businesses has a capacity of one two-way
trunk and one outgoing trunk from the turret to the subscriber's PBX and one incoming
trunk from the PBX to the turret. The incoming customer calls are received at the PBX
board and routed over trunks to the proper department turret, where an attendant re-
ceives the customer's request. The turret serves as a small switching unit between a
single telephone in the departments thus equipped and the PBX, and it avoids the in-
stallation of several telephones at each location.
An order turret system, where incoming calls are concentrated in one line-up of turret
positions, is also available. Incoming customer calls from either a manual or dial central
office or PBX are received in incoming trunk circuits, allotted by an allotter circuit to a
sequence storing circuit, and thence released to an idle attendant in the sequence in which
the calls are received. Thus the calls are distributed automatically as rapidly as turret
attendants become idle and with mimmum loss of time in handling. This type of system
has a capacity of 120 incoming trunks (with first group of selectors), 110 attendant's trunk
circuits, and 110 attendant's positions. A small order turret located in front of each at-
tendant has four keys and two lamps, a trunk, and a calling waiting signal for receiving
and originating calls. Calls can be held, released, or transferred bjr means of these keys.
Usually a manual or combined manual and dial PBX board is associated with this turret
system. Power supply is 20-28 volts direct current, for which a local automatic power
plant is provided. Hinging current is usually furnished over cable pairs from the central
office.
SECTION 18
TELEGRAPHY
THEORY
ART. -^T J°HN D. TAYLOR PAGB
1. Methods of Transmission 02
2. Codes 02
3. Telegraph Signals 05
4. Wave Shapes 05
5. Distortion 11
TELEGRAPH SYSTEMS
BY JOHN D. TAYLOR
6. Direct-current Systems 18
7. Automatic Telegraph Systems 26
8. Alternating-current Telegraph Systems. 35
9. Fac3imile System 38
10. Miscellaneous Transmitting and Signal-
ing Systems 38
SUBMARINE CABLE TELEGRAPHY
BY JOHN D. TAYLOR
11. Cable Data 41
12. Operation 42
TELEGRAPH EQUIPMENT
Axrm BY JOHN D. TAYLOB PAGm
13. Central-office Equipment 46
14. Station Equipment 51
TRANSMISSION-MAINTENANCE
BY JOHN D. TAYLOR
15. Transmission Standards 53
16. Transmission Coefficients 54
17. Crossfire 54
18. Maintenance 55
RADIO TELEGRAPH SYSTEMS
BY J. L. FINCH
19. Choice of Transmitter and Receiver Sites 56
20. Choice of Frequencies 56
21. Reduction of Fading Effects 57
22. Radio Interference 58
23. Frequency Shift Keying 58
24. Traffic Office and Equipment 5S
25. Control Channels 60
18-01
TELEGRAPHY
THEORY
By John D. Taylor
Fundamentally, the process of communicating by telegraph consists of sending electrical
impulses by wire or radio from a transmitting to a receiving point. These impulses are so
selected, arranged, and transmitted (in sequence) , that they are received, interpreted, and
recorded as intelligible characters at the receiving point. Such interpretation may be
made by the ear listening to the click of a telegraph sounder or the tone in a head receiver
or loudspeaker, or by automatic and mechanical devices.
Basically, it was necessary to develop codes (intelligence-bearing arrangements of elec-
trical impulses) and to provide transmitting and receiving devices and interconnecting
channels, capable of satisfactorily passing these codes between the desired locations.
1. METHODS OF TRANSMISSION
Telegraph codes or signals are transmitted electrically (1) by open-wire land lines or
cables or short submarine cables, using either direct or alternating current, (2) by long
submarine cables (oceanic), using only direct current, and (3) by radio, using only alter-
nating current.
Direct-current telegraphy employs a d-c source of power, which is either interrupted,
reversed in polarity, or altered in magnitude by the transmitting mechanism. The line
current frequency with present high-speed telegraph systems does not usually exceed about
200 cycles per second, and thus systems using this type of transmission are generally
referred to as low-frequency systems.
Alternating-current telegraphy employs, for each transmitting channel, a relatively
narrow band (about 170 to 300 cycles wide) of a-c frequencies, which are modulated by
the telegraph signals, being transmitted, before being applied to the line. A basic block
of frequencies, approximately 3000 cycles wide, is used to provide a group of carrier chan-
nels, the number of channels per block depending on the width allocated to the individual
channels. Carrier telegraph systems utilize one, two, four, or more basic blocks of fre-
quencies in each direction of transmission, the blocks being stacked one above the other in
the assigned frequency range by translation or second-modulation, as discussed in article 3,
Section 17.
The transmission and reception of signals may be either manual or automatic. In
manual operation, the transmitted signals are formed by a hand-operated switch or sending
key, and the signals are received either on an electromagnetically operated sounder, which
converts the signals into audible clicks, or on a Morse recorder, which makes an ink record
of the received impulses. These audible or recorded signals are interpreted by an opera-
tor, who typewrites the message manually. Automatic operation provides for the forma-
tion and transmission of the signals by an automatic circuit-interrupting device or trans-
mitter, which may be controlled either directly or indirectly by a group of keys similar to
a typewriter keyboard. The received signals are automatically interpreted and recorded
in typewritten form by a printer. In some cases, notably in the operation of submarine
cables, a combination of automatic transmission and manual reception is employed.
The transmitting and receiving equipment, and the associated line terminal apparatus,
are so closely related that the entire assembly is usually referred to as a telegraph system.
2. CODES
Characters of the alphabet, figures, and punctuation marks are transmitted as combina-
tions of marking and spacing impulses. A marking signal or impulse is one which causes
the receiving apparatus to be operated, and a spacing signal, which separates successive
marking signals, places the receiving apparatus in the unoperated condition. Spacing
signals may be intervals of no current, impulses of opposite polarity to the marking sig-
18-02
CODES 18-03
nals, or impulses of different current value from the marking signals. Two-element codes
employing only two conditions of current, positive and negative, or current and no cur-
rent, are mainly used on land line circuits. Three-element codes, which use both positive
Telegraph Codes
Morse Continental Cable Morse
............... •- •- 4--o
-++4-0
-4— 4-0
............... -' ' -- • -+4-0
E ............... • • 4-0
£ ............... •-• -•-• ++-4-0
g ............... --- --- --4-o
? ............... - - - - - - - -M--H-0
\ ............... ' ' • • 4-+0
J ............... ---- ---- 4- --- 0
K ............... --- --- -+- o
*V .............. — - -• • 4— 4~ho
M .............. -- -- -- 0
N ............... - . _. _ + 0
O ............... - . --- --- 0
P ............... ..... - --- 4— -4-0
Q ............... .._. --- - --- 1 — o
R ............... • • - - -- 4— 4-o
S ............... - • - - - - 4-4-4-0
T ............... - - -0
U ............... - - - • - - 4-4—0
v ............... . . . _ . . . _ 4-4-4— o
W .............. • -- - -- 4 --- o
X ............... --- - -.._ _4-_{— Q
Y ............... . . .: - . -_ — 1---0
Z ............... .... --- . _
1 ............... ---- ----- 4- ---- o
2 ............... .._.. .. --- ++ --- 0
3 ............... ..._. . . . __
4 ............... . . . . _ ......
5 ............... --- ..... 4-4-4-+4-0
6 ............... ...... _ . . . . ^^^+4.0
7 ............... --- - --- - - — 4-4-4-0
8 ............... -.... ---- . --- +4-0
9 ............... _..- ----- ---- 4-0
o ............... - ----- ----- o
Period ........... - ---- • ...... ++ ++ ++
Comma .......... . — . — ._._._ -} | j
Semicolon ........ ..... _._._. — j j f-
Colon ........... --- • • --- * ' ' ---- l"j- +
Interrogation ..... —...—. • • -- - - 4 ^7"~"rj~
Quotation ........ .._. — . ._.._. •] r-j j-
Short figures used in Continental and Cable Morse Codes where no confusion would result'.
1.... - - 6....
2.... • - - 7.... --- - •
3..,. - - --- 8..--
4=.... .... - 9....
5.... - 0....
FIG. 1. Telegraph Codes— Morse, Continental, and Cai>le Motse
and negative polarities and also a zero or no-current interval to separate groups of im-
pulses, are employed chiefly on long non-loaded submarine cables, where the comparative
freedom from extraneous interference removes the chief objection to the use of a zero
interval for the separation of signal groups.
The Morse Code is used Almost, exclusively in the United States on hand-worked land
lines; the Continental Code has been adopted by almost all foreign telegraph administra-
18-04
TELEGRAPHY
submarine cables.
Characters
Code signals-
tions, and is universally employed on radio telegraph circuits. In these two codes, the dot
signal is the basis of time measurement. A dash is three times the length of a dot; the
spaces separating successive impulses in a combination are of dot length; the spaces be-
tween impulse groups are equal to three dots; and a space equivalent to six dots is used
to separate words. The Cable Morse Code is used almost entirely in the operation of long
All impulses and spaces are of equal length, a positive impulse repre-
senting a dot and a negative impulse repre-
senting a dash.
In calculating speeds, the average Morse
character is equivalent in length to approxi-
mately 8.5 impulses of dot length, or about
4.25 cycles, while Continental characters
average about 9 impulses or 4.5 cycles each.
The Cable Code averages 3.7 impulses or
1.85 cycles per letter. These figures take
into account the frequency with which the
various letters of the alphabet occur in
ordinary telegraph traffic.
Figure 1 shows the combinations of dot
and dashes used in the Morse and Conti-
nental Codes, and the positive and negative
polarity and zero current intervals used in
the Cable Morse Code.
While the Morse and Continental Codes
are designed for manual operation, the
Cable Morse Code is transmitted automati-
cally. The automatic transmission of tele-
graph signals is almost universally employed
for land line, cable, and radio telegraph sys-
tems, because of its greater speed and ease
of operation, resulting in large economies.
Manual operation, when and where used, is,
in general, confined to short-haul traffic and
special services of such a nature as not to
warrant or be adaptable to automatic
operation.
In developing automatic telegraph sys-
tems, it was necessary to design machines or
devices, which would automatically send
and receive electrical impulses (positive or
negative) and to devise individual arrange-
ments of these impulses, representing intelli-
gible characters. It was further required
that these arrangements could be set up
manually for transmission, and sent, re-
ceived, and interpreted automatically at
speeds suitable to the transmitting medium.
One type of sending and receiving device
for use in automatic systems is the teletype-
writer or teleprinter (described in detail in article 7 of this section), which utilizes a 5-im-
pulse code for each character with a single impulse for starting and also for stopping both
sending and receiving units between characters. The code devised for the teletypewriter,
which is practically identical with that of the teleprinter, is shown in Fig. 2, in which L.C.
and U.C. are abbreviations for lower- and upper-case characters on the typing keyboard
and the black and white spaces are the marking and spacing impulses, respectively. The
signal impulse lengths in milliseconds (ms) are also shown for different operating speeds
(words transmitted per minute) .
Of the 32 separate combinations available, using 5 equal-length impulses for each
character, the combination of all spacing impulses has no character assigned to it and is
not transmitted.
The line frequency for the teletypewriter operation depends upon the number of words
per minute being transmitted. For 60-speed transmission (about 60 words per minute)
the shortest signal element is about 0.022 sec (see Fig. 2) , and the line frequency is
I/ (0.022 X 2) = 22.7 cycles per second
Signal lengths In milliseconds Standard speed
FIG.
Teletypewriter Code
System)
(Courtesy Bell
WAVE SHAPES
18-05
3. TELEGRAPH SIGNALS
Electrical impulses must be formed by the transmitting device, transmitted through a
connecting medium, and finally received and interpreted by the receiving device, so that
the received message is identical with the original sent message and is efficiently trans-
mitted. However, owing to the electrical characteristics of telegraph circuits and asso-
ciated Apparatus, telegraph signal currents are generally more or less modified (electri-
cally) in transmission, and, if suitable corrections were not made, these modifications or
distortion would, in many cases, cause errors in the received message.
Telegraph signals, in d-c operation, are classed as (1) neutral (current flows over the
line in either direction for the operated or marking position and no current flows for the
non-operated or spacing position of the line relays) or (2) polar (current flows over the
line in one direction for the marking and in the opposite direction for the spacing position
of the line relays) . For either type of signal, the change of current from mark to space or
space to mark is known as a transition.
Time
A
4. WAVE SHAPES
NEUTRAL SYSTEM. The change in line current values, with respect to time, may
be plotted to show the wave shape of the telegraph signal for any telegraph circuit, as shown
in Fig. 3 for a neutral circuit transmitting the Morse signal (dot, dash) representing the
letter A. For such a circuit, A in
Fig. 3 shows the wave shape of the
current, if the times of building up
and decaying to the steady-state
values are neglected, B shows the
effect on the wave shape of series
inductance (line relay or composite
set winding) , and C shows, by the
shaded area, the additional effect
on the wave shape of the composite
set or other condensers.
With reference to C, Fig. 3, when
the telegraph sending key closes,
the inductance in the circuit op-
poses any sudden change in current
value, and part of the current is
diverted from the line to charge the
composite set condensers to about
the applied battery potential, as
the line current builds up to its
maximum value; when the key
opens, the current immediately
starts to decay and, although
r\ r
\
Time
0
FIG. 3. Wave Shape for Letter A — Neutral Telegraph System
(Courtesy Bell System)
partly sustained by flow of current from the condensers and the opposition of the induct-
ance to current change, shortly reaches its minimum value.
Current wave shapes are important factors, which affect telegraph relay performance
and adjustments. For any given relay, there is a definite operating and release (less than
the operating) current value for given operating conditions. Figure 4 shows a schematic
d-c circuit, containing a neutral type of telegraph relay, milliarn meter, battery, and rheo-
stat. The retractive spring tension is controlled by adjusting screw Si, the armature to
pole piece air gap by S2, and the armature travel distance by 83 and £4.
Figure 5 shows the effect of relay adjustments on operating and release current values
(indicated by the black dots, 0, R, 0i, and RI on the curves), and on the effective length
(T and TI) of the telegraph signal. In telegraph parlance, the shorter marking signals
are called "light" and the longer marking signals "heavy." In practice, relay adjust-
ments are made, as required, to provide satisfactory received signals from usually dis-
torted wave shapes, caused by the electrical or mechanical characteristics of the line and
associated equipment or changes therein.
Effective signal length might also be increased or decreased for a given neutral tele-
graph circuit with a fixed relay adjustment by raising or lowering, respectively, the applied
circuit voltage. However, since line current values are limited, in practice, by crossfire
18-06
TELEGRAPHY
into other telegraph circuits or by interference with telephone transmission, this method
of controlling the signal length is restricted and not usually employed.
FIG. 4. Schematic of a 0-c Telegraph Circuit with Neutral Relay (Courtesy Bell System)
Relay adjustments are also affected by line conditions, such as leakage of line currents
to ground through tree or other contacts or the direct capacitance between the line wire
and ground. In general, for open-wire telegraph circuits this leakage factor varies as among
* Relay operating1 points
TJme
A
lime
B
FIG. 5. Effect of Relay Adjustment on Telegraph Relay Operation (Courtesy Bell System)
wires and increases materially from the dry to wet weather condition. Figure 6a shows a
neutral telegraph circuit with grounded battery at one station and Fig. 66 the same cir-
cuit with grounded battery at both stations, and for both circuits the leakage to ground,
FIG. 6. Neutral Telegraph Circuits with Leakage to Ground (Courtesy Bell System)
which may be concentrated principally at one or more points or generally distributed along
the line, is represented by the resistance S.
WAVE SHAPES
18-07
Figure 7 shows leakage effects on the current curve for the circuit (Fig. 6a). The curve
in Fig. 7, A, represents the ideal condition of no leakage. The curve in B represents the
leakage current alone through S. Since the inductance through S is less than through
station B, the leakage curve in B is steeper than the curve in _-L, and this resultant, which
affects station A relay, may be about as shown in C. In this curve, the effective signal
length Tc is greater (heavier signal) than TamA. The leak S also shunts the path through
station B and tends to decrease the line current to this station, as well as to flatten the
current curve, as shown by D.
The wide variation of effective signal lengths, Tc and Td, through station A and B relays,
in series, would not occur if half of the total line battery voltage was applied at each sta-
tion, oppositely poled to the line, as shown in Fig. 66. Since each battery supplies current
to the leakage path £, but in oppo-
site directions, the resultant current
through this path will generally be
small and the line current through
the station A and B relays will be
more nearly equal and stabilized
than for single end battery feed, thus
improving signal transmission.
Telegraph current wave shapes
formed by direct current are, in
effect, somewhat similar to a-c wave
shapes and contain various harmon-
ics of the fundamental frequency, as
will be discussed later. Owing to
the normal line wire capacitance to
ground (irrespective of other leakage
paths), the a-c components of the
telegraph currents will be shunted, in
X
Time
A
Time
B
Time
C
Time
D
FIG. 7. Effects of Leakage on Current Curves for the Neu-
tral Telegraph Circuit of Fig. 6a (Courtesy Bell System)
some degree. Thus, the line capaci-
tance not only reduces the effective
current at the receiving station but
also tends to distort the current
wave shape and to limit the length of operating line section between repeater points.
As indicated in Fig. 5, the relay operating points occur on a current curve between
points of transition. The change from the spacing to the marking condition is designated
space-to-mark (S-M] transition, and the change from the marking to the spacing condition
is designated mark-to-space (M-S) transition. At the sending end of a telegraph circuit,
the S-M transition takes place when the key is closed, and the M-S transition occurs when
the key is opened.
There is a certain time delay from the closing of the sending key to the operation of the
receiving relay and from the opening of the key to the release of the relay. In the first
case, this delay is designated space-Jo-mark transition delay (S-MTD) and in the second
case, this delay is designated mark-to-space transition delay (M-STD}, as shown in Fig. 86.
In Fig. 8a the line capacitance is represented by the dotted condenser path to ground.
When the sending key is closed, this capacitance is charged by current flowing over the
line from the sending station, and the current is retarded in building up to its full value
by the inductance in the circuit, as indicated by the sloping wave shape in Fig. S6. The
current which flows continuously in the biasing winding of the receiving relay produces a
constant magnetic field tending to hold, in this particular circuit, the receiving relay
armature against its spacing contact. When a marking signal current is received, the
stronger opposing magnetic field set up by the larger marking current in the operating
winding of the receiving relay causes the relay armature to move to its marking contact.
Although the operating points of a relay depend upon its design and adjustments,
it may be assumed, for the purposes of this discussion, that the relays in Fig. Sa will
operate on 33 and release on 27 ma of direct current, or plus and minus 3 ma from the
30 ma of biasing current, as shown in Fig. 86. When the operating current increases to
30 ma, the effective operating current in the receiving relay is then zero, but when it
reaches 33 ma, operation occurs and continues until the line current, decaying on open
circuit, decreases to 27 ma, when the relay releases.
The S-MTD period is the time it takes for the operating current to increase from zero
to 33 ma, and the M-STD period is the time it takes for the current to decay from its max-
imum value of 60 ma to the release value of 27 ma. These periods vary from a fraction
of a millisecond (ms) to several milliseconds, being determined, for a given circuit and
adjustments, solely by the circuit characteristics. For a given circuit and operating condi-
18-08
TELEGRAPHY
tions, each transition delay (S-MTD) will be the same for repeated signals, and the same
holds true for each delay (M-STD) , but the S-MTD delays may not be equal to the M-STD
delays.
Each mark, of whatever length, begins with an S-M transition and ends with an M-S
transition. The S-MTD period reduces and the M-STD period increases the effective
Current In mils
o S g £
1TD->
*~ ~H
^- -»•
«-S-MTD -J
<-M-STD
/
\
/
\
Relay bias
f
\
*v
f
V | currents*
TV
40 60 80 100 120 140
Time in milliseconds
FIG. 8. (a) Neutral Telegraph Circuit and (&) Signal Wave Shape (Courtesy Bell System)
length of the mark, so that, if these two delay periods are equal, the length of the mark
will not be changed by transmission over the circuit. Each space, of whatever length,
begins with an M-S transition and ends with an S-M transition. The M-STD period
reduces and the S-MTD period increases the length of the space, so that, if these two
delay periods are equal, the length of the space will not be changed by transmission over
the circuit. The transmission of signals is considered perfect if the received effective
marks and spaces are exactly the same length as the sent marks and spaces.
POLAR OPERATION. Wave shapes in polar telegraph systems are affected by circuit
inductance, capacitance, and leakage somewhat as in neutral telegraph systems. Figure 9
Central office
Outlying point
Line
\AA/v — i — V\A/v —
T
HI;
•± -130V
FIG. 9. Simplified One-way Polar Telegraph Circuit (Courtesy Bell System)
shows a simple one-way polar telegraph circuit, arranged to send — 130 and + 130 volt
impulses from the central office (sending point) to an outlying receiving point, having
series line resistance and capacitance between the line and ground.
Assuming that the sending-end connections are adjusted to provide normally steady-
state line currents of +35 ma (marking) and —35 ma (spacing), as shown in Fig. 10, the
line capacitance to ground will delay the change of line current from spacing to marking
(S-M transition) and from marking to spacing (M-S transition) .
WAVE SHAPES
18-09
The M-S and S-M wave shapes (Fig. 10) are identical in form and symmetrically located
about the zero line, and the S-MTD and M-STD are equal. Thus, since the sending end
potentials are equal and of opposite
sign, since the circuit resistance re-
mains constant for both positions
of the sending relay armature, and
since the operating points of the g 20
receiving relay are symmetrically g.
located at about the middle of the 1 10
wave shapes, the received polar i 0
signals are unbiased. |
TELETYPEWRITER AND ^ -10
TELEPRINTER OPERATION. In | __
teletypewriter or teleprinter opera- <§ 20
tion, there are five equal length im- _3o
pulses, each of which may be nega-
tive (mark) or positive (space), in **40
accordance with the code of signals
(Fig. 2) for this type of operation.
2O 30 4O
Time in milliseconds
Telegraph
character to be transmitted. Two
additional impulses are sent with each character, one starting and one stopping the
machines.
If a series of impulses, representing, for example, the letter £>, are plotted with time as
the horizontal axis, as shown in Fig. 11, it will be noted that the wave shape, in the upper
Start 12345 Stop
Teletypewriter D Signal at 368
operations per minute
a D-cr Component
b First Harmonic 6.1
c Second 12.3.
J
A A
d Third 18.4
\
e Fourth 24.5
r\ r\ r\
/Fifth 30.7 -
\_7
g Sixth 36.8
h Seventh 43.0
i Eignth 49.1
J Ninth 55.2
A /\ s\ y\ /*\
I D-c Component-t-firet harmonic
(a-i-fc)0-6.1
Ci-f c) 0-12,3
V
n (wi-HZ) 0-18.4
o (w-4-e) 0-24.5
p (0-t-/) 0-30.7
k Tenth 61.4
FIG. 11. Analysis of Wave-shape Components of Teletypewriter Character D (Courtesy Bell System)
18-10
TELEGRAPHY
left-hand corner of the figure, which is impressed on the line at the transmitting end of
the circuit, has "square" corners. However, if such a wave is analyzed, it will be found to
contain an infinite number of component frequencies, all of which, in practice, cannot and
need not be transmitted to the receiving terminal.
Though a very simple receiving device might be used, if all the components could be
faithfully transmitted over a circuit, such a circuit could not be economically provided.
Also, with an ideal receiving device, it would only be necessary to transmit a maximum
frequency equivalent to that which considers the duration of each unit signal element of
the code as 1/2 cycle (1 cycle would be the time involved from the end of element 1 to the
end of element 3 of the square wave in the upper left-hand corner of Fig. 11). This con-
dition is closely approached for long submarine cable telegraph systems, where the high
conductor cost warrants expensive terminal equipment for reasons of efficiency and
economy. However, for land line teletypewriter commercial use, neither expensive cir-
cuits nor elaborate terminal arrangements are Justified, and the facilities and equipment
that are provided represent a compromise on a cost balance basis.
For good telegraph transmission with comparatively simple equipment, it is desirable
that the received signal contain a substantial part of the second and third harmonics of
the frequency of the unit signal element. For 60-speed teletypewriter signals, the shortest
signal element is 0.022 sec, which is equivalent to 1/2 cycle. The fundamental frequency
at this speed then would be I/ (0.022 X 2) = 22.73 cycles per second, the third harmonic of
which would be about 68.2 cycles per second.
If one teletypewriter character is continuously repeated at 60-speed, the signal wave
(there being one per character) repeats itself about 6.1 times per second, so that, for the
purpose of discussing the signal components in teletypewriter operation, the wave may be
considered as composed of a d-c component and harmonics of a fundamental frequency
of 6.1 cycles, rather than harmonics of the signal element frequency. Thus, in Fig. 11,
the left-hand column shows several of the more important harmonic components of the
D signal, their relative magnitudes and phase relationships, the first harmonic (curve 6)
being shown as a sine wave of the same time period as the overall signal; the right-hand
column shows the combined resultant of the d-c component and the overall signal har-
monics, added successively, as indicated.
Since the fundamental signal element frequency for 60-speed operation was shown previ-
ously to be 22.7 cycles per second, theoretically the character D could be interpreted correctly
by an ideal receiving device if components, in correct phase relation, up to and including
the fourth harmonic of the overall signal (curve o in right-hand column) were received.
In practice, overall signal harmonics up to about the tenth (corresponding to about the
third harmonic of the signal element frequency) are transmitted, which gives a signal wave
similar to curve r and which resembles somewhat the square-corner wave in Fig. 11.
* CARRIER TELEGRAPH. Carrier telegraph systems employ modulated alternating
currents of different frequency bands. The voice-frequency (low-frequency) system uti-
lizes the band of 255 to 3145 cycles
for 18 channels of 170 cycles per
channel. The modulated output of
this system may be impressed, if
desired, on broad-band telephone
carrier or radio channels of higher-
frequency bands, making use of such
channels for telegraph rather than
for telephone service. The high-
frequency system for telegraph was
the first one developed. It is for
open-wire facilities and operates in
three different frequency assign-
ments, all of which lie within the
overall range of 3.33 kc to 11.25 kc.
These systems will be described later
in this section.
As previously described, the basic
signal element is a square wave pro-
duced by making and breaking a d-c
A. Impressed telegraph current
B. unmodulated carrier current
0. Carrier after modulation
FIG. 12. D-c Modulation of Carrier Currents — Tele-
graph Carrier Systems (Courtesy Bell System)
sending circuit or by applying opposite potentials (one at a time) to the transmitting de-
vice. Generally, the carrier wave is supplied continuously to the transmitting device and
is interrupted (modulated) in accordance with the d-c signals being produced by the local
sending circuit and impressed on the carrier wave at this device. Figure 12 shows the
impressed telegraph current (polar operation), the unmodulated carrier current, and the
DISTORTION
18-11
modulated carrier wave. The received segments of carrier current signal are rectified in
the demodulator circuit, and the resulting unidirectional plate current pulses act on a re-
ceiving d-c relay. These received d-c current signals, being similar in pattern to the sent
d-c signals, actuate the receiving relay in accordance with the sent signal.
Since the sending d-c signal contains, for practical reasons, up to about the third har-
monic, which at 60-speed operation is about 70 cycles, both carrier sidebands transmitted
will also contain this band width, or, for both bands at this speed, the frequency spread
would be about 140 cycles. For higher or lower speeds, this spread would be greater or
less.
5. DISTORTION
An ideal (perfect) telegraph circuit reproduces telegraph signals at the receiving end
exactly as they are impressed at the sending end, with respect to length, but not necessarily
amplitude, of the component marks and spaces. The time of travel of the signal over a
circuit is usually not important, even though such time exceeds the duration of a unit
signal element.
Distortion in telegraph transmission is thus determined by comparing the length and
relative arrangement of the signal elements as sent with the length and relative arrange-
ment of such elements as finally delivered by the receiving device.
The overall or total resultant distortion of signals, for a given telegraph circuit, consists
of two principal types of distortion, namely systematic and fortuitous, which result from
a number of different causes and require different treatments in design and maintenance
work in order to meet service requirements.
Assume that a given telegraph character is sent continuously over a telegraph circuit
and that each repetition of the character is considered perfect as sent. Measurements of
the distortion of each of the unit marks (elements) in a large number of successive repeti-
tions of the character at the receiving end will generally indicate that the distortion differs
(1) from element to element in a given repetition of the character and (2) from character
to character for a particular element in the character. The average of a large number of
distortions for a particular element is designated as systematic distortion. The individual
departure of the distortion from the average for a given measured distortion is designated
as fortuitous distortion. The total distortion of each signal element is the algebraic sum
of the systematic and fortuitous
distortions and is the amount of Duration of sent signal elements (=100 3D
deviation between the sent and ~"
received signals.
Figure 13 illustrates roughly
for 10 repetitions (not enough for
a good average in actual cases)
the distortion which may affect a
marking signal of unit duration
as received. The average length
of received signal is shown to be
90 per cent of the sent signal,
resulting in a — 10 per cent sys-
tematic distortion which applies
to all the repetitions. The de-
parture of the individual distor-
tions from the average varies
between repetitions, as shown in
the right-hand column, and in
the left-hand column the result-
ant distortion is indicated.
Systematic distortion may be
divided into two component dis-
tortions, bias and characteristic,
for the purpose of analyzing and
treating the causes of this type of
distortion. The nature of these
components may be explained by assuming a telegraph system in which marks and spaces
are sent by means of currents equal in magnitude but of either positive and negative or
negative and positive sign, respectively, as desired.
Bias Distortion. Assume that the systematic distortion, as measured, is due to a higher
positive than negative sending-end potential, and that this fact results in lengthening
Duration of received sign a I elements
n- * -*• Systematic Fortuftoas
Distortion (exponent component
1st
1
-1
0%
-10%
9
2nd
>
J,
41056
Srd
-li
*
-10*
9
4th
*«
*
-1055
42056
•5th
-2C
)*
->*
4*
4«
*
-J*
430*
TtTi
-4C
,<
4*
-ail
8th
-«
*
J*
0
Q>h
-1
y%
j>*
0
10th
-3C
&
j*
-20*
i I
FIG. 13.
Average distortion^ LO % ^systematic com ponent
Systematic and Fortuitous Distortion (Courtesy
Bell System)
18-12
TELEGRAPHY
the marks when positive current is used for transmitting marks, and in shortening the
marks when negative current is used for transmitting marks. Then, interchanging the
functions of the two current conditions employed changes the sign of the systematic
distortion but not its magnitude and is called bias distortion, indicating a lack of sym-
metry in the circuit.
A marking bias is called a positive bias, and a spacing bias is called a negative bias; and,
since the lengths of the marks and spaces may be indicated in milliseconds (ms) , the amount
of bias may also be indicated in milliseconds by the formula (M-STD) — (S-MTD) =
ms bias, the first two terms being
mark-to-space transition delay and
space-to-mark transition delay, re-
spectively, and the sign of the result
(using this formula) being the sign of
the bias. Thus, for a given circuit,
if M-STD = 6 ms and S-MTD * 3
ms, the milliseconds bias is +3, in-
dicating that every mark, regardless
of length, will be increased 3 ms, and
every space, regardless of length,
will be decreased 3 ms.
Though a given ms bias condition
Current In mllllamperes
i-> w •£"• o> s
O Cn O tn o <-
—S-MTD's
•«$
p=V
/""
V
-M-STD's
A-
)
\
;
< T0 \
d
r
T
\
t>
|\
/
/ '
.
C
V
3 10 20
30 4(
FIG. 14o.
Time in milliseconds
Effect of Relay Biasing Current on Signal
Length (Courtesy Bell System)
is due to such factors as unequal
marking and spacing line currents,
ground potentials, and improper
biased relay adjustments, this con-
dition will remain constant for the
transmission of signal reversals (but not random signals) irrespective of the speed of
transmission. However, the effect of a given ms bias condition on transmission does vary
with the length of the transmitted marks and spaces. For example, in a manual telegraph
circuit the dashes (long marks) are about 3 times the length of the dots (short marks),
and both dashes and dots decrease proportionately in length with increase in speed of
transmission. Assuming first a slow speed, where the dots are 30 ms long and the dashes
are 90 ms long, a ms bias of -f-10 will lengthen the dots and dashes to 40 ms and 100 ms,
respectively, the ratio of dash to dot length still being 2.5 to 1. However, if, owing to
an increase in speed, the dots and dashes are shortened to 5 ms and 15 ms, respectively,
the same +10 ms bias would result in dots 15 ms in length and dashes 25 ms in length.
The ratio of dash-to-dot length would then be about 1.7 to 1, and greater difficulty would
be experienced in reading the signals than for the usual ratio of 2.5 or 3 to 1.
Figures 14a and b show the effects on signal length of relay biasing current and line cur-
rent variations. In the first figure,
the line current is held constant at
60 ma, while the normal biasing cur-
rent (line B) is increased (lineiA) and
decreased (line C). In the second
figure, the biasing current is held con-
stant and the normal line current is
increased (high line current) and de-
creased (low line current) . It is evi-
dent that, in the first condition, in-
creasing the biasing current decreases
the signal length and decreasing it
increases the signal length; and, in
the second condition, increasing the
line current increases the signal length
and decreasing it decreases the signal
length.
Characteristic distortion results
from various causes, which are usually different from those associated with bias distortion.
Assume a telegraph system, in which the sending battery potentials are equal and oppo-
site in sign and in which the marks and spaces are formed by corresponding currents,
equal but opposite in sign. Also, assume that, owing to the characteristics of the given
system, the current is slow in building up to the normal mark or space value. If the cur-
rent does not have time to reach its final value on the short signal elements, the first
mark following a long space may be shortened. Under this condition, it is obvious that
interchanging the functions of the positive and negative current will not alter either the
330
20
Time in milliseconds
FIG. 14&. Effect of Line Current Magnitude on Signal
Length (Courtesy Bell System)
DISTORTION
18-13
sign or the magnitude of the resulting distortion, and the distortion is called characteristic
distortion, indicating it is a function of the signal combination and fixed characteristics
oi tne system, which causes
remnants from a given signal
element to affect succeeding
elements.
Depending on the speed of
operation, telegraph signals
are frequently of insufficient
duration to permit the line
current for a given signal to
change from one steady state
to the other, i.e., from a maxi-
mum positive to a maximum
negative line current, or vice
versa. In such cases, the
transition M-S or S-M will
occur while the current is
changing, and this is desig-
nated as a changing-current
M-S or S-M transition, both
of which are shown in Fig. 15.
It will be noted that, for this
particular polar telegraph
system, the time for the line
1
k,
o
ao
§ 20
1 10
30 40
Time in milliseconds
A
£-10
-30
—40
"1 J
Steady-state
x1 — M-S transition
^
\
i
< — 20 ms-
>
/
\
S-MTD
Q m<;
!\
/
f
M-STD,
\
/
10
ms'
N
\
/
'Xs^ Changing current
^-S-M transition
N,
/
33 ms—
"*"*-— 4
10 20 30 40 50 60 70
Tlrjie in milliseconds'
B
current to change from one
steady-state condition to the
other is 33 ms, whereas the
duration of the marking or
spacing signal is only 22 ms.
The net effect on the signal
is to shorten it 2 ms, since the
transition delay at the start
of the signal is '10 ms (sub-
tracts from the signal length)
and at the end of the signal is
only 8 ms (adds to the signal
length). The total current change in either transition is 28 ma (+25 to —3 or —25 to
+3) ; but, if the transmitted signal had been longer than 22 ms, the line current would
have exceeded plus or minus 25 ma and at the end of the signal the transition delay
FIG. 15. Changing Current Transitions (Courtesy Bell System)
*•
O
30 40
Time in milliseconds
FIG. 16. Characteristic Distortion Effects on Signal Lengths at 40f 60, and 75 Speed Operation (Cour-
tesy Bell System)
would have been greater, up to the limiting delay, resulting from the line current in-
creasing, up to its steady-state value.
Also, if the transmitted signal had been less than 22 ms long, the line current -would not
have built up to 25 ma by the time the signal ended, and the transition delay at the end
18-14
TELEGRAPHY
of the signal would have been less than for 22 ms. Figure 16 shows characteristic distor-
tion effects on marking signal length at 40, 60, and 75 teletypewriter operating speeds.
The time required for the line current to change from its maximum negative to positive
value, and vice versa, is 33 ms, and the marking signals are 33 ms, 22 ms, and 18 ms long,
respectively. Changing current transitions take place for all except the 33 ms signal
(40 speed), for which the steady-state current values are just attained. It will be noted
that the S-MTD values are the same (10 ms) for all signal lengths, but the M-STD values
decrease with decreasing signal length. For similar spacing signal lengths, the M-STD
values would be the same (10 ms), while the S-MTD values would decrease with decreas-
ing signal length.
The amount of a changing current transition delay is thus dependent on the line current
value at the start of the transition, and this line current value depends on the signal length
or speed of transmission. The lengths of the received signals are obviously affected by
these changing current transitions, and the magnitude of the effect is inversely propor-
tional to the length of the sent signals. Since received short signals are shortened by this
effect, the distortion is known as negative characteristic distortion. An opposite effect is
possible, though not common, and may result, if the line current increases momentarily
at the end of each transition to a value exceeding the steady state, owing to circuit charac-
teristics and transient effects. This effect would tend to lengthen the received mark or
space signal and would be known as positive characteristic distortion.
Some of the principal differences between bias and characteristic distortion are given in
Table I.
Table 1. Differences between Bias and Characteristic Distortion
Type of Distortion Is Affected by
Type of Distortion
Bias, ms
Characteristic
1 . Length of signal
No
Yes
No, except in neu-
tral operation
Yes
No
Yes
Yes
No
Yes
No
Yes
Not appreciably
2. For a given length of signal, whether the signal is marking
or spacing.
3. Amount and arrangement of the circuit capacitance, induct-
ance, and resistance.
4. Unequal marking and spacing line currents.
Change in line current.
Change in receiving relay biasing current.
Ground potential difference between sending and receiving
end.
5, Speed of transmission
6. Usual operating variations, occurring frequently throughout
the day, such as voltage fluctuations and relays requiring
adjustments.
Measurements of systematic distortion, in practice, will usually indicate that both bias
and characteristic distortion are present, or the total measured distortion with the circuit
normal is:
SI (Total distortion, circuit normal) = C (characteristic) + B (bias)
and the total measured distortion with the reversed condition is:
S2 (Total distortion, circuit reversed) = C (characteristic) — B (bias)
The characteristic component is (Si + S^) /2, and the bias component is (Si — Sz) /2.
Referring to Fig. 17, assume that a repeated signal is being sent over a given circuit,
consisting of a marking element 1 unit long and a spacing element 3 units long. If no
distortion exists, this signal will be received exactly as sent. However, when measured
with the circuit normal, the unit mark is found to be 15 per cent too long, as shown at A.
If a measurement is now taken with the line conditions for marking and spacing reversed,
this unit mark is found to be 5 per cent too long, as shown at B. By formula, the char-
acteristic distortion C is 10 per cent, and the bias distortion B is 5 per cent, both with
signs positive or marking. If, with the line conditions reversed, the unit mark was found
to be 5 per cent too short, as shown at £', the characteristic component of the 15 per cent
marking distortion (shown at A) would be 5 per cent and the bias component 10 per cent,
both positive or marking.
In practice, systematic distortion is usually determined, with the same methods as above,
by measuring a repeated signal consisting of a short marking signal followed by a long
spacing signal for the normal condition and then a repeated signal consisting of a short
spacing signal followed by a long marking signal for the reversed condition.
DISTORTION
18-15
Una
•6 — signal — >
element — $.
•"-
u-
_j Cl
U-5*
} com
id
*=£%
*^cond
B
istortion with circuit
^CjwpTti pjis_intercha nged=Sg
distortion with circuit f
iditions intsrchaiTged=.S2
For A and B:
Characteristic distortion
For A and B:
Characteristic Distortion
BIas=
FIG. 17.
Though the sign of the final value of characteristic distortion, as computed, is not
important, the sign for bias distortion is always important and is indicated.
Fortuitious distortion is caused by such factors as crossfire, power induction, momentary
battery fluctuations, line hits, break key operation, and similar effects. This type of dis-
tortion acts to alter the received signals by various amounts in an irregular manner. In
transmitting miscellaneous signals, the combined effect of all distortion on the displacement
of received transitions may result in
signals, sometimes called "jitter," \* Total length of signal
because of their rapid variations, or
the effect may cause a complete
breakdown in signal transmission.
Total distortion, for any given tele-
graph circuit, is usually a combination
of its bias, characteristic, and fortu-
itous components, and the total distor-
tion determines the quality of telegraph
transmission. However, for reasons
of design and maintenance, it is usu-
ally desirable to determine also the
value of these components.
Telegraph distortion is usually
given as a percentage of a perfect sig-
nal element of unit length. For man-
ual operation, these elements or dots
are usually sent at a rate of 12 or 13
dots per second, and then* duration
(taking into account the dot length
interval between each two dots) is
about 40 ms. For 60-speed tele-
typewriter transmission, the signal-
ing rate is equivalent to about 22,7
dots per second, and the duration of
the unit signal element, in this case,
is 22 ms.
TELETYPEWRITER DISTORTION. Distortion as it affects start-stop teletypewriter
signals must be considered in a somewhat different manner from that for other types of
telegraph systems, because teletypewriter system operation differs fundamentally from
the operation of other systems. Each teletypewriter operation (the transmission of a
character), as previously described in this section, is initiated by the mark-to-space transi-
tion at the beginning of the start pulse of the received character. It is important that
each of the succeeding transitions in the character be correctly timed with respect to the first
transition. Distortion causes the displacing of succeeding transitions from their normal
positions with respect to the start transition and thus reduces the margin of operation of
the teletypewriter.
Bias distortion usually affects both the beginnings and ends of the received signal
elements. However, the teletypewriter receiving mechanism starts on a mark-to-space
transition (for each character received), and this transition is also affected by the same
bias, so that succeeding mark-to-space transitions in the character will not be displaced
with respect to the start transition, owing to bias. The space-to-mark transitions will be
displaced with respect to the start transition by an amount equal to the total bias. With
marking bias, all space-to-mark transitions will be uniformly displaced toward the start
transition, whereas with spacing bias they will be uniformly displaced away from the start
transition.
Characteristic distortion may displace both the received space-to-mark and mark-to-
space transitions with respect to the start transition, depending on the signal combina-
tion, and recurs for the same signal combination. It may affect both ends of the teletype-
writer orientation range, and when miscellaneous characters are received a distinction
cannot be made between the characteristic and fortuitous components of the distortion.
Fortuitious distortion displaces miscellaneous received transitions by various amounts
in a random manner, regardless of the signal combination. These effects may result in
errors in received characters or, if severe, in complete circuit failure.
The total distortion is the displacement of a received transition from its correct time of
occurrence, and it is equal to the algebraic sum of the fortuitous distortion and the systematic
distortion. The total distortion determines the margin of operation of the receiving tele-
typewriter, and it is a measure of the transmission quality of the received signals
Characteristic and Bias Distortion
Bell System)
(Courtesy
18-16
TELEGRAPHY
In teletypewriter operation, not only signal distortion takes place during transmission,
but also mechanical variations occur in the teletypewriter mechanisms which affect the qual-
ity of signal transmission. The mechanical operation of the teletypewriter is described
briefly in article 7 of this section, but, for the purpose of discussing distortion as it affects
teletypewriter operation, some of the mechanical features of the teletypewriter must be
referred to in this article.
Figure 18 shows some of the principal mechanical units of the selecting arrangement of
a teletypewriter which determines the instant, in the duration of a given received signal
element, when the actual selection takes place. For example, if the signal element being
received is marking, the selection must be made at some instant during the time this
Acnratore extensfoi
.ocktog fevar
;k!hg cam
larking bias
Spacing bias-
Distortions other
than bias
Send dist. 6.7% faster
than rec. dist.
a Send dist. 5.9.% slovyec
* than rec. dist.
FIG. 18. Distortion Effects on the Selection of Teletypewriter Signals (Courtesy Bell System)
particular element is being received, in order that the code bar, corresponding to this
selection, will be properly positioned and the character of which this element is a part
will be correctly recorded.
The selecting mechanism includes: (1) the line magnet, which is operated by marks
and non-operated by spaces; (2) the armature and armature extension, which are held in
the position shown during marking and are released to the dotted position during spacing;
(3) the stop latch, which stops the locking cam rotation after each revolution; (4) the
locking lever, whose point B, during rotation of the locking cam, engages one side or the
other of the end of the armature extension, depending on the position of the extension,
thereby locking the extension momentarily, which results in the code bars being properly
positioned; and (5) the locking cam, which is driven by a friction clutch and which, in a
single revolution, causes the locking lever to be positioned five times, once for each of the
five signal elements received, during the transmission of one character.
In the idle condition, the received signal is always marking and the magnet is energized,
but the selector cam assembly is held stationary by the stop latch until the start pulse
(always spacing) is received, when the stop latch is released and the cam starts rotating.
The speed of rotation and the starting position of the selector cam assembly are normally
so adjusted that the first depression on the locking cam (point A) will arrive at the locking
lever point (which rides the cam) at about the instant the middle of the first selecting signal
element is being received. At this instant the locking lever point (riding the cam) moves
into the cam depression, and the lever point B moves forward to lock the armature and
its extension in one of the two positions they may occupy at that instant. The position
of the armature extension determines which of the two line conditions, marking or spac-
ing, will be recorded for the signal element being received, and the position of the cor-
responding code bar. As the cam rotates, a similar selection takes place as the locking
lever enters each of the five depressions on the cam and the corresponding code bars are
positioned in succession. The final arrangement of the five code bars results in the selec-
DISTORTION 18-17
tion of one and one only type bar, which, when actuated immediately after completion of
one revolution of the locking cam, prints the sent character on paper. The final pulse of
the train of signal elements (for each character received) is always marking and somewhat
longer (1.42 units) than the preceding six elements (1.0 unit each). During this pulse, the
stop arm on the receiving selector cam assembly strikes the stop latch, and the assembly
is then held stationary until the next start pulse is received for the next character.
When a start pulse is received, a small increment of time will elapse before the selector
cam assembly attains full speed, owing to such factors as the inertia of moving parts and
clutch slippage. This delay is compensated for by slightly decreasing the distance between
the point at which the locking lever rests on the locking cam, and point A on the cam, from
what the distance would be if these factors were not present. This adjustment is repre-
sented by the distance x, as shown on the cam surface in Fig. 18.
The teletypewriter is usually equipped with an orientation or range finder device, which
permits rotating the stop latch with respect to the locking lever, thus changing the time
of selection with respect to the start signal. The range finder moves the stop position
either forward or backward and has a pointer which moves along a scale, the scale being
calibrated in percentage (0 to 120) of a unit signal element. If the pointer is moved toward
the lower-numbered part of the scale, the time between the start and selecting points is reduced
and the time of selection is advanced toward the beginning of each selecting element.
// the pointer is moved toward the higher-numbered part of the scale, the time between the start
and selection is lengthened and the time of selection is moved toward the end of each select-
ing element. For an ideal teletypewriter, whose mechanism acted instantly and selected
exactly the corresponding instant of each signal element, the range finder could be moved
over a range of 100 per cent, if perfect signals were received, without causing errors in the
received signals, as shown by (a) in Fig. IS. Moving the range finder, in effect, shifts the
solid vertical lines with respect to the signal elements, and for (a) the time of selection
could be changed, without error, by ±50 per cent. Practically, teletypewriter specifica-
tions require the overall range to be at least 72 per cent without error for perfect signals.
Distortion in teletypewriter signals, as previously stated, is usually some combination
of bias, characteristic, and fortuitous distortion. Theoretically, if bias exceeds 50 per cent
in (c) and (e) of Fig. 18T errors will result in the recorded signal, but, from a practical
standpoint, the bias tolerance is of the order of ±40 per cent with perfect received signals
because of allowances that must be made for other variations.
Internal bias may exist in a teletypewriter as the result of such factors as improper
adjustment of the line relay or receiving magnet. This bias reduces the orientation margin
more when receiving perfect signals than when receiving signals with a bias equal in
magnitude but opposite in sign. In order to minimize tin's bias effect, the range finder
should be set at the point where signals having equal marking and spacing bias just cause
errors.
The effect of shortening the start pulse by 25 per cent, (f) in Fig. 18, is equivalent to
lengthening the stop pulse and retarding the points of selection for the succeeding signal
elements by the same amount. The effect of shortening the end of the stop pulse by 25
per cent (g) is equivalent to advancing the points of selection for the succeeding signal
elements by the same amount. The effect of advancing the beginning of element 1 and
of retarding the beginning of element 3 and the ending of element 4, as shown by (&), will
not result in errors in the received character if the range finder is set at its midpoint. The
effect of speed variations where the sending machine is faster than the receiving machine is
illustrated by (i)» and where the reverse is true is shown by 0")- The most probable error,
in both cases, would be in the proper selection of element 5, since, in the first condition,,
part of the stop pulse is received on the 5 position, and, in the second condition, either
element 4 is extended into position 5 or element 5 is so delayed in starting that it would
not be properly received in its normal position. The effect on teletypewriter margin of
speed variation is mostly at one end or the other of the orientation range, depending on
the relative speeds of the sending and receiving machines. Though the speed differences
in Fig. 18 are shown large for purposes of illustration, actually these differences are nor-
mally about 1/2 per cent or less.
The orientation range limits are determined by the various distortions present for a
given teletypewriter circuit. It is not possible to judge these distortions quantitatively
by the limits obtained when more than one type of distortion exists. However, assuming
low machine bias, these limits do give a good indication of the quality of the received
signals. If the limits are reasonably definite, some fixed distortion, such as bias or speed
difference, is generally present, while, if there is a certain range at each limit over which
certain characters are consistently in error, characteristic distortion is indicated. If there
is a range over which errors occur, but not consistently on certain characters, fortuitous
distortion is most likely present.
18-18
TELEGBAPHY
TELEGRAPH SYSTEMS
By John D. Taylor
Telegraph systems employ various types of telegraph equipment and connecting
mediums and various methods of transmission. Direct-current telegraph systems are
used extensively in land wire operation and in conjunction with radio channels, while
low- and high-frequency carrier telegraph systems utilize both land wire lines and radio
channels as mediums of transmission. Radio telegraph systems make use of radio channels
between radio transmitting and receiving equipments and usually wire line extensions
between such equipments and the telegraph circuit terminals.
6. DIRECT-CURRENT SYSTEMS
Open-wire telegraph channels are generally obtained by using bare telegraph wires.
They may also be provided by simplexing or compositing open-wire telephone circuits, as
shown in Figs. 1 and 2,
Station A Station B
Simplex coll
Telephone line circuit
Sounder
respectively.
The simplex arrange-
ment is shown in Fig. 1.
The arrows represent the
telegraph line currents,
which divide equally at
the junction of the two
halves of the line wind-
ings of the repeating coil
at A and travel over both
line wires of the telephone
circuit to the repeating
coil at B, where they
again combine at the
«. i j ^ -, , ^. .. ,^ x junction of the two halves
5n Simplexed Telephone Circuit (Courtesy *f ,-, • •-. -i..,. &
Bell System) °* ™s COL^ De*ore passing
to Station B telegraph
equipment. This equal division of the current is possible only if the two halves of the line
side of each coil are identical electrically and the two line wires have identical electrical
characteristics. To the extent that these conditions are not met, the current will not
divide or combine equally at the coils and a residual induced current will flow in the drop
windings of the repeating coils, causing interference (Morse thump) in the telephone cir-
cuit. In practice, Morse thump becomes objectionable only when faults occur.
_ , _ . , _.
FIG. 1. Telegraph Circuit
Telegraph
.Retardation colls
Telegraph leg
Line T-TJT
wire 4rXjrl:
FIG. 2. Telegraph Circuit on Composited Telephone Circuit (Courtesy Bell System)
The composite arrangement is shown in Fig. 2. One grounded telegraph channel is
obtained from each line wire of the telephone circuit by connecting composite sets at each
terminal of the circuit in such a manner as to maintain the balance of the circuit and
DIRECT-CURRENT SYSTEMS
18-19
avoid excessive telegraph, current flow in the
line and drop windings of the repeating coils,
which current would cause Morse thump. The
equipment on the two sides of the circuit must
be well balanced and the line wires must be
closely identical electrically to prevent tele-
graph signals from interfering with the tele-
phone service. With this arrangement each
telegraph channel is independent of the other
and is usually so operated.
The composite set has a retard coil in series
with the telegraph leg and capacitance between
the leg and ground to prevent sudden changes
in signal current value being impressed on the
line wires and causing current surges (clicks) in
the telephone circuit. Also, the series condens-
ers in the telephone circuit prevent direct cur-
rent from reaching the repeating coils and
assist in reducing clicks, while the retard coil-
condenser bridge on the drop side of the series
condensers functions to prevent crossfire, a con-
dition where the telegraph signals on one wire
of the circuit induce potentials on the other wire
that interfere with the telegraph signals over it.
A schematic diagram of a neutral telegraph
circuit is shown in one form in Fig. 6a, article 4.
This circuit operates with current flowing in
either direction for the marking condition and
no current flowing for the spacing condition.
Both sending and receiving relays usually
operate local sounder circuits, which produce
the recognized audible dots and dashes of the
Morse or Continental telegraph codes by the
armature of the sounder striking its front and
back contacts, corresponding to the marking
and spacing conditions. Neutral telegraph
operation is also employed in teletypewriter
and teleprinter service on many of the shorter
circuits.
The receiving station may break the circuit
(stop the transmission of signals) by opening
the sending key, which silences both sending
and receiving sounders and indicates to the
sending station that the receiving station de-
sires to send signals.
A number of intermediate stations may be
connected in series in the single wire line, the
number depending on the sensitivity of the line
relays, the battery voltages applied, and line
conditions, such as resistance and leakage.
The single line repeater, a schematic dia-
gram of which is shown in Fig. 3, may be
employed over long single wire circuits. This
repeater functions to receive weak signals from
the line from either direction and repeat them
with normal voltage to the line in the other
direction. The signal transmission circuit
through the repeater is shown by heavy lines.
Operation of the west station key causes relay ' A
to repeat signals to the east circuit, and operation
of the east station key causes relay A' to repeat
signals to the west circuit.
Opening either station key interrupts current
flow in both east and west lines, and, unless aux-
iliary circuits were provided in the repeater,
18-20
TELEGRAPHY
both circuits would open and remain open, and the system would be inoperative. To
prevent this condition, a biasing and a locking circuit are provided (see Fig. 3) for each
direction of transmission. Each biasing circuit operates the armatures of the line and
control relays, with which it is associated, to spacing, when the circuit through the line
windings of these relays is opened during the transmission of signals. However, the lock-
ing circuit is so designed that, for east-to-west transmission with the east circuit open, the
biasing current reverses direction in the biasing windings of the line west relays and the
armatures of these relays are held on marking, thus maintaining the east circuit closed at
the repeater, regardless of the position of the east station key. The locking circuit func-
tions oppositely for west-to-east transmission.
A break feature (see Fig. 3) is provided, so that the receiving station may interrupt the
sending station, as desired, by opening the receiving-station key.
The one-way polar telegraph circuit, shown in Fig. 9, article 4, usually employs — 130
volts for marking and +130 volts for spacing signals to a distant polar receiving relay.
This circuit operates from the central office to an outlying point and is used in certain
cases where a one-way service only is required, such as in the transmission of news copy.
Two -path polar operation consists essentially of two one-way polar circuits operating in
opposite directions.
Polarential operation provides for true polar operation from the central office to an
outlying point and a modified polar operation in the opposite direction. The advantages
of polar over neutral operation (particularly self-compensation of line leakage) are thus
obtained with relatively simple equipment arrangements at the outlying point.
Figure 4 shows a type A polarential telegraph circuit, in which true polar signals are
transmitted from the central office, and ground and —130 volt battery (in series with a
i*— 1
^+130 V.4
Central office
FIG. 4. Type A Polarential Telegraph Circuit (Courtesy Bell System)
total added resistance of 990 ohms) are applied in transmitting marks and spaces, respec-
tively, from the outlying point. In this case a repeater is not used at the outlying point,
as is more commonly done in type A operation.
During transmission from the central office, the circuit is closed to a direct ground at
the outlying point through the sending contacts (in this case, the contacts of a teletype-
writer) while the central-office receiving relay is held on its marking contact by a marking
biasing current. This current is adjusted to one-half the effective spacing current when
a spacing signal is being sent from the outlying point. During transmission from the out-
lying point, the ground, applied for a marking signal, has no effect on the central-office
receiving relay, provided that the line and artificial line are balanced at the duplex set,
and this relay is held on its marking contact, while negative battery, applied through the
resistance for a spacing signal, produces an effective spacing current in the central-office
relay. This current is the net result of current flowing in the central-office relay windings
from (1) the outlying-point battery and (2) the central-office battery, due to the duplex
balance being upset by the 990-ohm resistance in series with the outlying-point battery.
The variable resistance R at the central office is adjusted so that the spacing line battery
at the outlying point is higher than the potential applied to the apex of the duplex at the
central office, thus insuring line current reversal when a spacing signal is transmitted from
the outlying point and home copy if a teletypewriter is employed.
Figure 5 shows a simplified type B polarential telegraph circuit, in which true polar
signals are transmitted from the central office, and ground and +130 volt battery are used
in transmitting marks and spaces, respectively, from the outlying point. This circuit is
more nearly self-compensating for line leakage than the type A circuit.
When transmitting from the outlying point over a dry (no leakage) line, the marking
DIRECT-CURRENT SYSTEMS
18-21
line current does not affect the central-office receiving relay, if the balancing network at
the central office exactly balances the line electrically.
For a spacing signal from the outlying point, aiding positive battery, applied to the
line, results in an effective spacing current 28 /(Ri -f R£, where E is the outlying battery
potential and RI -f- JtJ2 = RL are as shown in Fig. 5. The marking biasing current in
the central-office receiving relay is adjusted to a value equal to E/2Rz,.
Central office
FIG. 5. Type B Polarential Telegraph Circuit (Courtesy Bell System)
During transmission over a wet line with leakage Rg (shown at P on the line), Ra (at
the central office) may be adjusted to maintain the potential at the apex of the relay wind-
ings at the same value as for the dry condition when transmitting a spacing signal from
the outlying point. Thus, as a result of the compensating effects of the Ra adjustment,
the received signals at the central office are not affected. If RI is greater than 2R*, com-
plete leakage compensation is not possible, unless the central-office battery voltages are
made higher than the outlying battery voltage or other compensation is provided. For
this purpose, Rb is provided for maintaining RI less than 2R%.
The bridge arm, with a resistance in series with condenser C, is provided at the outlying
point to neutralize reverse current surges through the receiving relay winding when the
outlying sending relay armature moves from space to mark. Such surges would tend to
cause false breaks (kick off) of the receiving relay and mutilation of the home copy.
Metallic telegraph circuit operation, generally utilizes telegraph cable pairs or open
wires, or, when telephone facilities are involved, it is customary to composite them to
secure the necessary telegraph channels. The avoidance of interference between telegraph
FIG. 6. Four-wire Metallic Telegraph Circuit (Courtesy Bell System)
and telephone circuits and of crossfire between telegraph circuits in cables generally re-
quires that the telegraph current values be comparable to those on the telephone circuits
and that metallic circuit operation only be employed. Such operation may employ two
wires or four wires, pairs, side circuits, or phantoms.
In four-wire operation, as shown in Fig. 6, separate paths are employed for the two
directions of transmission, and artificial balancing lines are not required, as in two-wire
18-22
TELEGRAPHY
operation. These differences generally improve transmission over that of the two-wire
arrangement, since balance between the conductors and an artificial line is not a factor.
Owing to the use of four composited channels, as compared to two such channels for two-
wire operation, the possibilities for conductor and equipment troubles are greater with
four-wire operation. In general, four-wire telegraph circuits may be superposed on two-
wire telephone circuits of lengths ranging from about 500 to 1000 miles, or on longer four-
wire telephone circuits. Very long four-wire telegraph circuits are not composited through-
out their entire length because of prohibitive low-frequency delay distortion introduced by
the composite sets.
Duplex systems may be of the earlier bridge type or the later, more commonly used
differential type. Both these systems employ arrangements of telegraph apparatus for
terminating telegraph circuits at the central office which permit the simultaneous trans-
mission of telegraph signals in both directions over a single wire with ground or metallic
return and without the signals in one direction interfering with those in the opposite
direction.
Since bridge polar duplex operation is rapidly being discontinued and is expected to be
of little interest in the future, its description is omitted from this handbook. However,
occasional reference is made to it for purposes of comparison in the following paragraphs,
which relate to differential polar duplex operation.
Figure 7 shows schematically the differential type set, arranged for full duplex operation.
The receiving relay has two equal windings, one being connected in the real line and the
Receiving relay
I Line
Receiving
loop
FIG. 7. Terminal Differential Duplex Set Arranged for Full Duplex Service (Courtesy Bell System)
other differentially in the artificial line circuit. Sending current from the station battery
divides at the apex of the receiving relay windings and flows equally in the real and in the
artificial line circuits, assuming these are balanced. Since the receiving relay windings
are differentially connected, the station receiving relay is not affected by this current flow.
However, current from a distant station does operate the receiving relay at the home
station, since it flows through the windings of this relay in a series aiding relation from
the line through the balanced arms and the artificial line to ground. Similarly, the re-
ceiving relay operates at the distant station from incoming line current from the home
station. Under these conditions full duplex operation is attained.
In the differential-type duplex set, the sending relay has both an operating and a biasing
winding. With the sending loop key closed, the magnetic fields produced by these two
windings are opposing, but a resistance R in series with the biasing winding limits its cur-
rent to about half that in the operating winding and the armature is accordingly held to
the marking contact (negative) . When the loop key is opened, only the biasing winding is
effective and the armature moves to its spacing contact (positive) .
Duplex systems, employing the ground for one side of the circuit, are affected by varia-
tions in line constants due to temperature and humidity changes, but the balancing
artificial lines associated with each duplex set usually may be adjusted to compensate for
such variations. Duplex systems provide all the advantages of polar operation in both
directions of transmission, but they also necessitate higher-grade supervision and greater
maintenance than some of the simpler systems, such as in neutral operation.
The differential duplex system has largely superseded the older bridge duplex system
because of several advantages of the differential over the bridge type. The differential
system includes a simple differential duplex repeater for use at intermediate points on
long telegraph circuits; in. the bridge system, two terminal sets, requiring considerably
DIRECT-CURKENT SYSTEMS
18-23
more equipment, must be used at such points. Intermediate differential repeaters may
be employed on circuits having bridge polar type sets at their terminals, or bridge polar
intermediate repeaters may be used- on circuits having terminal differential sets at their
terminals.
One of the most important advantages of the differential over the bridge system is the
ability of its polar relays to respond rapidly to signals, particularly at the higher operating
speeds. These relays, in addition
to being more sensitive than the
relays ordinarily used in bridge
polar sets, have a special third
winding which forms part of a
vibrating circuit and materially
increases the relay response. The
vibrating circuit, shown, in Fig.
8, includes the third winding of
the receiving relay, whose arma-
ture is connected to the midpoint
of the winding. One outer ter-
minal of this winding is grounded
through a condenser, and the
other outer terminal is grounded
through a resistance. Batteries
*«>-«• m^ota*tnS-WB-wW»^B-i
contacts.
Assuming that no current is flowing in either the line or artificial line windings of the
receiving relay, the relay armature moves back and forth continually between the two
contacts. However, with current flowing in the line and artificial line windings in normal
operation, the armature does not vibrate freely as before, but the vibrating circuit aids in
speeding up the armature action, as the received line signals cause it to move between its
marking and spacing contacts. The free speed of vibration is governed by the parameters
C and R, which are usually adjusted so that the frequency of vibrations is slightly greater
than the line signal frequency.
Half duplex operation, which provides for operation in only one direction at a time,
requires a means for breaking the circuit from either terminal and for utilizing one loop
for both sending and receiving signals. Either the bridge- or differential-type system may
be employed for this service, but each requires a different circuit arrangement of the duplex
set from that required for full duplex operation. In the bridge-type system, the principal
additions required are a control relay, holding coil for the pole changing relay, and a re-
peating sounder; for the differential-type system a control, break, and neutral relay are
added. The change from full duplex to half duplex, or vice versa, for either system is
readily accomplished by means of switches provided with the duplex sets.
Figure 9 shows a schematic diagram of a terminal differential duplex arranged for half
duplex service. The control relay functions on incoming signals to prevent the sending
2R| R
f
relay UOJ-
J
P
Loop
FIG. 9. Terminal Differential Duplex Set Arranged for Half Duplex Service (Courtesy Bell System)
relay from operating when the loop is opened and closed by the receiving relay. Two
oppositely poled batteries are connected to the biasing winding of the sending and break
relays, and the resistances R and 2R are so adjusted that, with the control relay contact
18-24
TELEGRAPHY
closed, the positive (spacing) battery will be in control and the sending relay will operate
in the same manner as in full duplex operation.
When signals are being received from the line, a marking signal closes the loop, and
current flows from the loop through the sending relay operating winding. When a spac-
ing signal opens the local loop at the receiving relay contacts, no current can flow through
the sending relay operating winding. However, the control relay also operates in unison
with the receiving relay (since their windings are in series) , opening the positive (spacing)
battery at its armature contact and permitting negative (marking) battery to take con-
trol of the sending and break relays through resistance 2R. Thus, the sending relay arma-
ture is held on its marking contact for either incoming marking or spacing signals.
If the local operator wishes to break the circuit while incoming signals are being re-
ceived, the local loop circuit is first opened by opening the sending key. The next spacing
signal received with the loop open would be ineffective, since the signal would normally
open the loop at the receiving relay contact. The next marking signal received with the
loop open would operate the receiving and control relays, and positive (spacing) battery
would be applied to the biasing windings of the sending and break relays through the con-
trol relay armature contact and resistance R. Since there is no current flowing through
the operating windings of the sending and break relays with the loop key open, both relays
operate to spacing. Positive battery is then applied to the line through the sending relay
spacing contact, which results in a break signal to the distant operator.
The break relay functions to insure a continuous break signal to the line as long as the
local loop key is open, regardless of subsequent signals received from the line. Assuming
that one of these signals is a spacing signal, the receiving and control relay contacts will
open, which would permit negative (marking) battery to take control of the sending and
break relays and marking battery to be applied to the line through the sending relay mark-
ing contact if a secondary circuit was not provided. Marking battery applied to the line
would interrupt the break signal. However, positive current is maintained through the
biasing windings of the sending -and break relays as soon as the break relay operates to
spacing (which it would do on the preceding incoming marking signal), since positive
battery is then applied through the neutral relay, spacing contact of the break relay, re-
sistance R, and the biasing windings of the sending and break relays to ground.
The neutral relay in this secondary circuit functions to prevent the possibility of the
circuit becoming inoperative owing to the sending and break relays at both terminals
becoming simultaneously operated to spacing. Under this condition, neither operator
could regain control of the circuit, since the loop circuits at both terminals would be open
at the receiving relay contacts. Operation of the neutral relay which occurs when the
control relay is opened after the break relay is operated to spacing short-circuits the re-
ceiving relay contacts, so that the sending and break relays will be operated to their mark-
ing contacts when the associated loop key is closed.
The upset duplex method of operation between a central office and an outlying point
employs polar transmission generally from the central office to the outlying point and
Central office
Outlying point
S M
FIG. 10. The Upset Duplex Method in Telegraph Operation (Courtesy Bell System)
neutral transmission in the opposite direction. Transmission in either direction is affected
by line leakage, and transmission to the central office is subject, in general, to the same
limitations as for a neutral circuit employing a single line repeater. Because of polar
operation in one direction and the application of wave-shaping units at the outlying point
only, this method offers an improvement in operation over the neutral circuit with a single
line repeater.
Figure 10 shows the upset method of operation, employing a duplex set, arranged for
half duplex operation at the central office and a teletypewriter (neutral operation) at the
DIRECT-CURRENT SYSTEMS
18-25
Schematic of Intermediate Differential Duplex Repeater
(Courtesy Bell System)
outlying point. ^The teletypewriter normally operates on 60 ma of line current in an open
and close loop circuit, and its line relay requires a spacing biasing current of 30 ma. The
algebraic sum of the marking and spacing line currents while sending to the outlying
pouit must equal 60 ma, in order to meet the requirements for operation under the upset
method Also, when receiving at the central office (neglecting the effects of series induct-
ance and bridged capacitance on the line), the effective spacing current in the receiving
relay with the outlying point key open must equal the effective marking current in this
relay with the outlying point key closed. In practice, it is generally necessary to adjust
these spacing and marking currents in the receiving relay, since the inductance and
capacitance effects cause unsymmetrical wave shapes and cannot be neglected.
The duplex repeater is employed at intermediate points in long circuits to maintain
proper operating currents in duplex telegraph systems. The distance between repeater
points depends on a number of fixed and variable factors, such as the type of line facilities,
interference from extraneous sources, line leakage, coordination of transmission levels,
types and quantities of central-office equipment involved, line operating speeds, and
maintenance considerations.
Figure 11 shows schemati-
cally an intermediate differ-
ential duplex repeater circuit
for grounded operation.
For 60-speed start-stop
teletypewriter operation, the
maximum lengths of single
composited line sections of
104 mil and 165 mil copper
line wire, over which it should
be practicable to operate
either the differential duplex
or two-path polar systems
without intermediate repeat-
ers, will be roughly within
the range of 170 to 300 miles and 250 to 450 miles, respectively. For any given section,
the maximum length depends on a number of variables, such as the types and quantity
of terminal and intermediate equipment used, the line conditions, and maintenance
schedules and type of personnel.
Where thump, nutter, and crossfire considerations permit, 60-speed differential duplex
or two-path polar operation is usually feasible in cable over a composited 13 or 16 gage
wire with crossfire neutralizing networks or over a 19 gage simplexed pair or phantom for
distances up to about 100 miles.
The quadruplex system permits four messages, two in each direction, to be transmitted
simultaneously over a single grounded circuit. One transmission in each direction is
secured in the same manner as has been previously described under the heading Duplex
Systems, article 6. These two channels and the associated sending and receiving appa-
ratus are called the polar side of the quad. The two additional transmissions (one in each
direction) are obtained by varying the strength irrespective of the direction of the line
current, and by receiving the signals, thus sent, on a neutral relay, which responds to
impulses of large amplitude irrespective of polarity but remains unaffected by impulses
of smaller amplitude. These two channels and the associated equipment are designated
the neutral or common side of the quad.
The schematic circuit of the differential quadruplex is shown in Fig. 12.
Normally a resistance is in series with the pole-changing relay, and a leak to ground is
connected to the line, to preserve the proper ratio between the marking and spacing cur-
rent of the common side. When this resistance is short-circuited, and the leak resistance
removed by the contacts of the transmitting relay, in response to the operation of a send-
ing key which controls it, the line current is increased to its maximum value. The neutral
relays in the receiving circuits are adjusted so that they will respond to the stronger
signaling currents but will be unaffected by the weaker ones. Momentary release of the
neutral relay at the instant the direction of line current is reversed by operation of the dis-
tant pole-changing relay is prevented by the discharge of a condenser through a special
holding winding.
The normal operating currents in a quadruplex set are 10 to 20 ma for the polar relays
and 30 to 60 ma for the neutral relays. A ratio of 1 : 3 or 1 : 4 between the spacing and
marking current is required to insure good operation.
Although employed quite extensively at one time, the quadruplex system is now used
but little, because it was found impossible to maintain uninterrupted operation of the
18-26
TBLEGEAPHY
To Neutral Side
Sending Key.
FIG. 12. Differential Quadruples Set
common side during periods when damp weather or other causes lowered the line insula-
tion sufficiently to reduce the ratio between the operating and non-operating currents.
The common side of a quad is also more susceptible to interruption by inductive inter-
ference from adjacent circuits.
The bridge principle, described under duplex systems, may also be utilized in a quadru-
ples system.
7. AUTOMATIC TELEGRAPH SYSTEMS
Start-stop systems, employing the teletypewriter and teleprinter equipment (similar type
units of the Bell System, and Western Union Co., respectively) for sending and receiving
telegraph signals, are so named because of the method of operation. This equipment
usually employs the seven-element code, of which the first element is a start pulse, the
seventh element is a stop pulse, and the other five elements represent the character. Thus,
the sending and receiving units are synchronized after each group of seven pulses (ele-
ments) is received, constituting the transmission of a character.
Usually, the teletypewriter or teleprinter installation at a subscriber location consists
of an electromechanical unit, with or without a keyboard resembling that of a standard
typewriter, and having a typing mechanism for printing received messages on a paper page
or tape. At receiving-only stations, the sending keyboard is not required. In some cases,
the subscriber may perforate a tape, using a keyboard-equipped perforator, the perforations
representing coded characters of the desired message. This tape may at the same time or
later be passed through a tape transmitter, which, being connected to the line, sends pulses
over the line corresponding to the characters of the message. Also, incoming code pulses
may be received by a reperforating machine, which perforates a tape with the five-element
code representing the received characters. Figure 13 shows a sample of perforated tape.
trerase - ? : $ S ! & JE 8 .,ȣ
Lower Case ABQDEFQHi J KLMNOPQRSTUVWXYZoSJEJ
Feed Ho
1
5
:• • • • • •
• • « » • • •
.....;..,.%...;.;,, .;...;.....;.
: *• •:. •••:•:.
•
•t
•'
•
•
•
;-
•
•
•
•
• •
;•••
•
•
•
•
•
•*
':•'
FIG. 13. Teletypewriter Code Perforated in Tape
The teletypewriter sending unit now in general use consists principally of a keyboard
with key levers extending over five notched selector bars, and a start-stop mechanism of
driving and driven shaft, universal bar, cams, eccentrics, levers, and pawls. Figure 14
shows the general mechanical arrangement of the start-stop mechanism.
Figure 15 shows the details of the key lever, which, when pressed down, positions the
selector bar, which, in turn, moves the locking latch head forward or back. This latch will
either prevent the contact lever from closing the transmitter contacts (latch head forward) or
permit the contact lever to close these contacts ' (latch head back) , when the associated
AUTOMATIC TELEGRAPH SYSTEMS
18-27
selector cam depression arrives at the proper projection on the contact lever. Thus, as a key
lever is depressed to send a particular character, the universal bar is moved down, causing
the mechanism (Fig. 14) to function and the selector cams to start rotating. At the same
time, the five selector bars and locking latches are positioned by the key lever, and each
Cam sleeve assemb
_, L , Throw cut cam
Clutch spring , Drlyen jay/
Driving ]a
lutch lever eccentric
'lutch lever
Clutch lever pawl
Universal bar Selector bar
FIG. 14. Start-stop Mechanism of Teletypewriter Sending Unit (Courtesy Bell System)
of the five contact levers is either locked or left unlocked, so that, as the selector cams
make one revolution, each set of transmitter contacts does not close or does close. If the
contacts do not close, a spacing signal (no current) is sent over the line, and if the con-
tacts close a marking signal (current) is sent over the line.
Release of the key lever after it has been fully depressed causes the driven jaw to be
thrown out of engagement with the driving jaw upon completion of one revolution of the
'lector cam
Key lever
Selector bar
latch
Key
Contact levei
Transmitter contai
Selector
i lector cam
ing latch
FIG 15 Positioning of Transmitter Contacts by Operating Key Lever of Teletypewriter Sending Unit
(Courtesy Bell System)
cams, and the rotating movement stops- The mechanism is now ready to send the next
character.
The teletypewriter receiving mechanism now generally employs a single selector magnet
and a group of six rotating cams, so spaced angularly on a shaft that each cam functions
at the instant the corresponding signal pulse is being received.
Figure 16 shows the mechanical arrangement for translating the selector magnet opera-
tions into the positioning of the code bars. When the open pulse is received, the magnet
armature releases. This operates a latch (not shown), allowing the cam shaft to rotate.
The spacing of the cams on the shaft is such that, as the first of the five pulses of the code
18-28
TELEGRAPHY
signal is being received, the first cam engages the projection on t'he code bar operating
lever associated with the first code bar and rotates it slightly in a counterclockwise direc-
tion. Assuming that the received No.
1 pulse is marking, the armature will
be operated, and the movement of the
code bar operating lever will lift the
sword and cause its upper right-hand
projection to strike the right-hand end
of the armature extension. The sword
will then rotate in a clockwise direc-
tion on its pivot at A, so that, when
the selector cam clears the code bar
operating lever and allows the latter's
spring to return it to normal, the sword
point will be forced against the left-
hand projection of the T lever, rotat-
ing it hi a counterclockwise direction
and moving the No. 1 code bar to the
right. If the received No. 1 pulse had
been spacing, this code bar would have
been moved to the left.
In like manner, the other four code
bars are properly positioned and the
sixth cam releases a clutch, allowing
the printing mechanism to operate, as
shown in Fig. 17. The five code bars
have been positioned to the right or
left in accordance with the five code
pulses received, which represent a par-
ticular character. The code bar slots
-. ,- m . . _ . . », , . wiU then *me UP so tnat the Putt bar
FIG. 16. Teletypewriter Receiving Selector Mechanism. .<• j.u 4. «u „„* -n « 4. • w-i,
Illustrating Portioning of Code Bars (Courtesy Bell for that character wiU center m these
System) and only these slots and will engage
the main bail. This bail is then moved
forward, causing the pull bar to move forward and the type bar head to be driven against
the paper or tape in°the teletypewriter.
After completion of one revolution of the rotating cams, the rotating movement stops,
owing to action of the stopping mechanism, and the teletypewriter is then ready to re-
ceive the pulses for the next character.
Type bar
T lever
FIG. 17. Teletypewriter Receiving Mechanism, Illustrating Selection of Symbol (Courtesy Bell System)
Power for mechanically operating both the teletypewriter and the teleprinter is gen-
erally secured from the 110-volt commercial supply at their location, these machines
AUTOMATIC TELEGRAPH SYSTEMS
18-29
being equipped with either d-c motors, a-c series motors, or a-c synchronous motors. The
last type of motor is available for use with 50- or 60-cycle power and is the preferable
type where the power frequency has the usual close regulation. The power consumption
is about 115 watts at 115 volts.
The line signaling circuit usually requires about 60 to 70 ma of direct current for magnet
and line relay operation, and the remote control circuit (if provided) about 50 ma.
The regenerative repeater may be employed (1) at intermediate points in long com-
mercial or private line teletypewriter circuits, (2) at points where it is desirable to divide
a teletypewriter circuit into several sections because of possible distortion from a large
number of sending stations connected to the circuit, and (3) at teletypewriter exchanges
for switched connections and for furnishing service to subscriber teletypewriter loops
having a relatively high transmission coefficient.
Start-stop teletypewriter signals, composed of one start and five signal pulses of equal
unit length and one stop pulse of 1.42 units length (teleprinter signals are composed of
seven pulses of equal unit length), are sent from the originating motor-driven distributor
or other sending device with mechanical precision. However, as these signals progress
over a telegraph circuit several telegraph repeater sections long, the distortion accumu-
lates section by section, so that, unless corrected, the distorted signals received at the
circuit terminal would result in message errors.
The regenerative repeater located at one or more intermediate points in a long teletype-
writer circuit, as required, retimes and reshapes the received distorted signal pulses and
retransmits them, as though they were directly from the originating machine.
Figure 18 shows a schematic of the circuit for one two-way regenerative repeater
arranged to repeat signals from east to west or west to east, but not in both directions
West receiving relay West.east
regenerator unit
Notes:
@ Indicates common 130-voIt 120-ohro
positive battery tap.
Q Indicates common 130-voIt 120-ohm Q
negative battery tap
FIG. 18. Schematic Circuit of the Regenerative Repeater, Arranged for Half-duplex Operation (Cour-
tesy Bell System)
simultaneously. For full duplex operation, the circuit requires two one-way regenerative
repeaters. The loop circuits are arranged to receive and transmit neutral signals from
the terminal duplex telegraph repeaters between which the regenerative repeater is usu-
ally connected. Each loop termination contains the line winding of a polar receiving
relay and the sending contacts of a regenerator unit in series. Each receiving relay arma-
ture controls a local battery circuit to energize the magnet of the regenerator unit through
the marking contact. When the receiving relay armature moves to its spacing contact,
the receiving relay armature in the opposite loop is locked to marking.
The regenerator unit has both sending and holding contacts, the latter being controlled
by a cam in such a way that they are open only when the cam assembly is near the stop
position. During retransmission of the signal elements of a complete character, the hold-
ing contacts, being closed, apply battery of opposite polarity through a potentiometer to
the receiving relay biasing winding of the loop, into which the signals are being retrans-
mitted. Reversal of current in this biasing winding holds its armature to marking, thus
preventing repetition of the retransmitted signal back through the regenerative repeater
toward the originating terminal.
18-30
TELBGEAPHY
Sendin
Since the length of the retransmitted signals is timed mechanically by the locking cam,
the outgoing signal length is normally independent of the incoming signal length. As
long as that part of the received pulse corresponding in time to the release of the magnet
armature is not affected by distortion, the outgoing pulse will be undistorted.
Tlie multiplex system, a development of 1915, functions to divide the line facility time
of a given telegraph channel (between two terminal points) among several telegraph cir-
cuits. The usual manually operated teleprinter (or teletypewriter) circuit line signal speed
is inherently much less than the speed capabilities of a high-grade telegraph trunk. To
utilize such capabilities efficiently, the trunk time may be allotted among two, three,
four, or more telegraph circuits on a full duplex basis. When four transmitting and four
receiving terminals are operating simultaneously at 66 words per minute over one trunk
line, this line is handling 528 (8 X 66) words per minute, thus enormously increasing its
efficiency over single teleprinter circuit operation. One multiplex channel may be oper-
ated in each direction over a duplexed circuit or carrier channel, each of which provides
two separate telegraph paths. This system, because of its high efficiency of operation, is
generally employed over heavily loaded telegraph trunk lines.
A code is used in which every character consists of 5 equal-length impulses, each of
which may be either positive or negative, thus yielding 32 separate combinations. The
code as it appears in a perforated transmitting tape is shown in Fig. 13. The black dots,
representing perforations in the tape, correspond to marking impulses, and the blank
spaces correspond to spacing impulses. One of the 32 possible combinations, 5 positive
or spacing impulses in succession, has no character assigned to it, and is transmitted con-
tinuously when no messages are being sent. Two combinations, designated "letters" and
"figures," are used respectively to cause the
printer to print lower-case or upper-case
characters, thereby increasing the total num-
ber of characters that may be transmitted.
A schematic of this system is shown in
Fig. 19. Each of five contacting levers in a
transmitter is connected to correspondingly
numbered equal-length segments of a dis-
tributor, which are successively connected to
the line through the rotating brushes Ff Fr
and an unsegmented collector ring B. Dur-
ing the time the brushes are traversing
another part of the distributor, the trans-
mitter levers are positioned to correspond
with perforations in the transmitting tape.
Receiving) 0,,-^iM M,M '*, After the brushes have passed over those
segments and transmitted the signal com-
bination to the line the tape is advanced to
the next set of perforations and the cycle
of operations is repeated. Auxiliary or local segments (not shown) in the distributor are
used to step the transmitter ahead at the proper point in each revolution of the distributor.
The received signals operate a polarized relay, whose armature applies current from a
local generator to the brushes /, f of a receiving distributor, which comprises a solid col-
lecting ring Bf and a segmented ring A.' . Five segments of this ring occupying about the
same angular position as the sending segments are connected to five correspondingly
numbered magnets which control the operation of the printer. The sending and receiving
brushes at opposite ends of the line are rotated in nearly exact synchronism, and their
angular positions are so adjusted by automatic means that the receiving brush will make
contact with one segment at the instant a pulse is received from the similarly positioned
sending segment, thus operating the corresponding selecting magnet. Therefore, at each
revolution of the brushes the five printer magnets will be operated in sequence to repro-
duce the identical combination set up on the transmitter levers.
One or more additional sets of transmitters and printers, similarly connected, provide
several independent channel transmissions during one complete revolution of the brushes,
so that by proper choice of the number of channels the full capacity of a line may be uti-
lized, while the individual channels are operated at speeds that will not exceed the capabili-
ties of the operators or apparatus.
The transmitters are controlled by a perforated sending tape (Fig. 13), prepared by the
operator on a perforator which has a keyboard similar to that of a typewriter. Two types
of printers are used. One, known as a page printer, is similar to a typewriter and
is equipped with automatic means for returning the carriage and for feeding the paper to
print the message in page form; the other prints the message in a continuous line on a
Distributor Selecting Magnets
FIG. 19. Schematic Diagram of the Multiplex
System
AUTOMATIC TELEGRAPH SYSTEMS
18-31
narrow paper tape, which, is gummed on the reverse side to permit of its being readily
pasted on message forms.
Distributor brushes are rotated by a synchronous impulse motor of the LaCour type,
which is supplied with impulses of constant frequency generated by the contacts of an
electrically driven tuning fork. Slight variations in motor speed are compensated for by
applying a precise phase correction controlled by intelligence signals received from the
distant terminal. Since synchronism is maintained between the sending and receiving
terminals, the standard start and stop pulses (of the teleprinter) are not required for the
multiplex circuit, but other local control pulses are employed.
Multiples channels are operated commercially at speeds from 50 to 80 words per minute
(one word averages 5 letters and a space, which is equivalent to 15 cycles per word).
The number of channels used is determined by the traffic load and type of circuit avail-
able. On duplexed land lines a maximum of four channels in each direction is permissible.
Three channels can be satisfactorily operated on carrier channels spaced 170 cycles apart,
and four multiplex channels may be applied on carrier channels spaced 200 cycles apart.
Two to eight channels may be successfully operated on submarine cable, depending on
the type of cable and terminal equipment.
The line frequencies for various speeds and number of channels in each direction are
given in Table 1.
Table 1. Line Frequencies
5-letter
Words per
Minute
Line Frequency, cycles per second
8 Channels
6 Channels
4 Channels
3 Channels
2 Channels
50
60
70
80
100
120*
140*
160*
75
90
105*
120*
50
60
70
80
37.5
45
52.5
60.0
25
30
35
40
* Not used commercially.
Special repeaters are not required for the operation of multiplex on duplexed circuits
less than 1000 miles long, as the regular duplex repeaters are usually satisfactory. On
longer circuits, or in those which contain more than three duplex repeaters in succession,
the signals are likely to be distorted sufficiently to cause frequent errors and require exces-
sive attention to the apparatus. In such circuits a regenerative repeater is usually em-
ployed at every third or fourth repeater point.
The varioplex system, a Western Union Telegraph Co. development, is an automatic
telegraph system which provides for the connection of up to 40 individual telegraph cir-
cuits or subchannels, having variable message loads, over a single high-capacity telegraph
trunk circuit, to other individual telegraph circuits or subchannels at one or more distant
points. The actual number of subchannels operated over a single varioplex trunk is
limited mainly by practical considerations, one important factor being the total message
load presented to the trunk at any one time.
Though the cost of this service to the patron is relatively low, the patron has, in effect,
a private high-grade telegraph connection to the distant party. The installation for
each patron consists of a sending teleprinter and a receiving teleprinter, thus providing
simultaneous two-way service. Character counters, connected to the sending legs of
each subchannel, determine the number of words sent, for billing purposes.
Messages are transmitted over a given subchannel by operating the keyboard of the
sending teleprinter, and messages are received over a separate subchannel and automati-
cally printed by the receiving teleprinter on a page or tape. Any patron may send a
message at any time, as desired, and the other patrons in a given varioplex system may
do likewise. All the messages are received at the central office in the varioplex terminal
equipment and transmitted in sequence over the varioplex trunk to its distant terminal,
which automatically distributes each message to the proper distant subchannel, over
which it reaches the patron for whom it is intended.
The varioplex terminal equipment may be classified as (1) individual to each subchan-
nel, (2) common to all connections, and (3) part of the varioplex trunk circuit.
Figure 20 shows a schematic of a two-channel (A and B) varioplex circuit with^ eight
patron offices and teleprinters TPR at each terminal of the circuit for one direction^ of
transmission only. The opposite direction is similarly provided. The principal equip-
ment units at sending terminal X for each subchannel include a reperforator RPF, tape
transmitter XTR, sending chain relays SA and &B, and sending control relay SCO. Com-
mon equipment units include two banks (five relays per bank) of sending relays A and B
and a segmented distributor sending ring (five segments per varioplex circuit channel).
18-32
TELEGRAPHY
The principal equipment units at receiving terminal Y include, as common equipment, a
segmented distributor receiving ring (matches the segmented sending ring), two banks
(five relays per bank) of receiving relays A and B, and two local transmitting devices TA
and TJB (each an arrangement of vacuum tubes) . The individual subchannel equipment
includes receiving chain relays RA and RB and receiving control relay RCO.
Five sending and five receiving relays (banks A and A or B and B of Fig. 20) are asso-
ciated with the five respective segments of each channel. These relays function in such
a manner that, if teleprinter characters are being sent by one or more patrons at station
X, positive or negative potentials will be applied by each relay to its corresponding seg-
ment at station X, causing positive or negative pulses (combination determined by the
Varioplex System
Station X
Station Y
FIG. 20. Schematic of Two-channel (Double-type) Varioplex Circuit (Courtesy Western Union Tele-
graph Co., Electrical Communication and O. E. Pierson)
character being sent) to be transmitted over the line to station Y, as the sending brushes
pass over the segments connecting them, one by one, to the line.
At station Y the distributor brushes rotate in close synchronism with the distributor
brushes at station X, and each receiving segment is connected through the line, for a
short interval of time, to its corresponding sending segment on the distributor rings. As
the pulses are received at station F, the receiving relays are operated or released, depend-
ing on whether the pulses are positive or negative.
The relay RA or RB of a given subchannel will operate in unison with the relay SA or
SB of the corresponding sending subchannel and will remain operated during selection of
a character by the receiving bank relays A or B. The two relays RA and RB of each
subchannel control their subchannel circuit through their contacts. This circuit is closed
to a fixed potential, when both relays are in their released positions, but is disconnected
from this potential and is connected to device TA or TB, upon operation of RA or RB,
respectively. Devices TA and TB are controlled by the contacts of the bank relays
A and B, respectively, and by a segmented ring (simplex ring) of the receiving distributor.
Assuming that a given RA relay is in its operated position, pulses from the receiving
simplex ring segments actuate the input circuit of the vacuum tube unit TA in accordance
with the selected character stored in relay bank A, causing a signal combination to be
transmitted over the connected subchannel to the associated teleprinter, which prints the
character sent.
AUTOMATIC TELEGRAPH SYSTEMS 18-33
No distinction is made with respect to which varioplex channel is used for the transmis-
sion of a character from any given sending teleprinter. Successive characters are sent
alternately over the two channels, one character being supplied by each subchannel in
turn. _ After all patrons who are sending have transmitted one character, the cycle of
operation is repeated. Successive characters from a given subchannel may be trans-
mitted over either varioplex channel.
Relays SA and SB operate in a cyclic manner, characteristic of the counting chain
type of relay circuit. A local ring of the distributor furnishes two pulses per revolution,
one pulse for operating each chain relay. Each chain relay is locked in its operated posi-
tion after being actuated by one of these pulses, andt whenever any chain relay is actu-
ated, any other previously operated relay in the same vertical row (Tig. 20) is released.
Not more than one SA or SB relay is operated at one time. Also, the circuit is such that
not more than one relay can be operated in the same horizontal row. If all eight sub-
channels were sending at the same time, the chain relays would operate progressively
upward, starting with SB relay 8, then SA relay 7, SB relay 6, and so on. Thus, in four
revolutions of the brush each of the eight sending subchannels would transmit one char-
acter. This cycle of operations would be repeated as long as signals were being sent.
The SCO and RCO relays operate in unison, by means of special signals sent over the
line, to remove from the operating chain circuits their associated SA and SB and RA and
RB chain relays, respectively, when these chain relays are not functioning. This removal
does not affect the other chain relays, which are operative. Thus, by controlling the SCO
and R CO relays, so that they remain operative if traffic is available at the transmitter, and
inoperative if such traffic is not offered, the main line circuit time is made available only
to those subchannels having a simultaneous need for it, and the cycle of operations is
speeded up. The SCO relay is controlled through a collating arrangement which "reads"
the character in the transmitter, causing the sending control relay SCO to operate or re-
lease, depending on the type of character.
If the line between stations X and Y is capable of transmitting satisfactory signals at
a rate of 800 characters per minute, the two distributors for the two-channel varioplex
circuit are adjusted to a speed of 400 rpm. This method may be employed for all high-
speed automatic circuits to divide the total traffic capacity of a circuit into smaller and
more practical components.
Reperforator switching systems are primarily switching arrangements for use in large
message relay centers. These systems not only reduce to a minimum the time required
in relaying messages through such centers but also substantially increase the message
capacity of trunk lines and facilitate personnel training problems. This equipment is
now in operation in a number of the main telegraph centers in the United States, and
installations are in progress in other large centers.
The reperforator switching system of recent design consists principally of: (1) receiving
equipment, which prints the incoming characters on and perforates them hi a tape; (2)
crossoffice trunkmg circuits, by means of which the received message is transferred to a
sending position; and (3) the sending equipment, which retransmits the message to its
destination or to a second relay center.
Incoming and outgoing transmission as handled by the reperforator-switching system
is usually at the rate of 66 words per minute; the rate over the crossoffice trunks is 150
words per minute, thus permitting rapid clearance of messages from the receiving posi-
tions. The high rate over the crossoffice trunk is due to the use of a five-wire trunk, per-
mitting the sending of a five-element character at a time. Since the attendant has only
two switch operations to perform in order to relay a message through an office having
this system, the time required in handling the message is only a matter of seconds. The
message is passed through the office entirely on tape, no manual receiving or sending
being involved.
If an outgoing channel selected for the transmission of a message is idle at the time of
selection, there is no delay at this channel in retransmitting the message. If the channel
is busy and no other channel is selected for the message, the tape from the sending re-
perforator is automatically stored in a specially constructed narrow glass compartment
and is fed out through the line transmitter automatically, as soon as the busy channel is
available.
Special centers, known as "spillover" and XV centers, of the switching office are pro-
vided to handle messages that are abnormally delayed for various reasons, such as circuit
trouble, destination office closed, incomplete address, and uncertain routing, or to handle
messages of an emergency or special nature. These centers contain switching turrets and
printer perforator receiving positions of the same general type, as previously described.
Sub center switching systems (Western Union Telegraph Co.) are employed, where a
number of branch offices and private line patrons are localized in an area some distance
18-34 TELEGRAPHY
from the nearest main switching center. In order to eliminate delays in handling the
messages originating from these sources, and to reduce operating costs which would occur
if the messages were collected at a local office by messenger or otherwise and thence trans-
ferred to a switching center, subcenter switching units, as required, are installed in such
areas to extend the local lines automatically direct to the main switching center over a
small group of trunks. Usually the number of trunks required is about one-third the
number of local telegraph stations served.
In this sytem, the patron's teleprinter sends outgoing messages to the main switching
center direct, the local line being automatically switched through the subcenter. A direct
circuit from the main center to the patron is established for incoming messages by the
main-center attendant dialing the patron's line number over an idle subcenter trunk,
which is automatically connected to the patron's line through switches at the subcenter.
In Teletypewriter Exchange Service (TWX) in the Bell System, line concentrating
units are usually employed for serving areas, such as described above. These units are
arranged for automatic switching of two-way message service between a group of sub-
scriber lines at an outlying center and a manual teletypewriter switchboard over a small
group of trunks. One such unit has a capacity of 30 lines, which appear on the verticals
of three 10 by 10 crossbar switches. The trunks appear on the horizontals of these switches.
A 100-line unit is also available.
Private line switcHng and intercommunicating systems are useful in extensive tele-
graph leased wire networks, such as are employed to connect a number of widely located
stations and offices in large industries or governmental agencies. These systems perform
a service in handling telegraph messages somewhat comparable to that which private
branch exchanges perform in handling telephone messages. The systems are attractive
to large users because of their simplicity to operate and freedom from trouble.
The larger private line switching systems of the Western Union Telegraph Co., receive
messages on printer perforators, which feed the perforated tape into a sending tape trans-
mitter. This transmitter is connected to the desired outgoing line by means of a plug-
ended cord and jack.
When a message is being received at a given unit, the attendant notes its destination
on the tape and inserts the plug of the cord circuit associated with that unit in one of
two multipled jacks in which the outgoing line terminates. Two jacks are provided for
each line so that, if one of the jacks is in use and a second message is received for that line,
the connection may be made for this message in the idle jack and the message will be sent
as soon as the first message has been cleared.
Perforator and transmitter units are frequently provided for the patrons, where it is
desired to prepare messages in advance by perforating them in a tape and transmitting
them at the same time or later.
Fully automatic message switching systems in which the first characters of the code
serve to control the switching equipment have been developed and are now in operation.
Intercommunicating systems, as provided by the Bell System for private and govern-
mental users, employ teletypewriter station equipment and teletypewriter switchboards,
at which connections between stations or between a station and a trunk are established manu-
ally by means of cord circuits. The operator is provided with a teletypewriter by means
of which incoming calls are answered and outgoing connections are established by typing
on a keyboard. The station may have a page type sending-receiving teletypewriter, or a
sending-receiving typing reperforator, for printing characters on and perforating them in
a tape (11/i6-in. wide), with which is associated a transmitter-distributor, or other com-
binations of sending and receiving equipment may be provided.
Teletypewriter Exchange service (TWX), as established throughout the United States
by the Bell System for public use, provides both large and small switching centers inter-
connected by trunk circuits of "suitable grade.
Thus, two TWX subscribers, being provided with the necessary equipment, may com-
municate with each other by written message from one part of the country to another
over a vast network of lines and equipment, somewhat similar to that established for
nation-wide telephone service.
Transmission limitations, with respect to overall connections, are important factors in
furnishing a satisfactory general teletypewriter exchange service, as discussed in article 16.
Teletypesetting, a process of automatically setting type, is accomplished by perforating
in a tape the copy material to be set in type, and then feeding the perforated tape into a
transmitting device which actuates a typesetting machine. The tape may be perforated
locally or by a perforator receiving automatic signals of the proper code over a telegraph
circuit from a distant point. The six-unit code is used in the transmission of the charac-
ters, and special teletypewriter or teleprinter equipment arranged ta send and receive this
code is employed, providing page copy for checking purposes.
ALTERNATING-CURRENT TELEGRAPH SYSTEMS 18-35
8. ALTERNATING-CURRENT TELEGRAPH SYSTEMS
Alternating-current telegraph systems employ both wire and radio channels for the
transmission of telegraph signals.
Voice-frequency carrier telegraph systems operate within the lowest carrier frequency
(voice) range of about 250 to 3150 cycles.
One such system, now in common use, provides up to IS two-way telegraph, channels
having carrier frequencies from 255 to 3145 cycles, spaced 170 cycles apart. This particu-
lar system operates on a four-wire line basis over various types of facilities, such as loaded
four-wire cable circuits, open-wire physical circuits on a four-wire basis (noise conditions
permitting), and the different types of carrier telephone channels under suitable condi-
tions.
Figure 21 shows the principal elements of a telegraph channel from the sending to the
receiving telegraph terminal for the particular eighteen-channel system referred to above.
At the sending terminal, the marking signal closes the line circuit at the step-up trans-
former and the carrier current is transmitted over the line to the receiving terminal, where
it is amplified and detected, and finally operates the receiving relay to marking < — ) . For
Sending Receiving Amp. det. Receiving
filter filter level comp. relay
D-c telegraph
circuit
-<s— 1
From d-c
telegraph circuit
Sending relay
PIG. 21. Principal Elements of a Carrier Telegraph Channel (Co-urtesy Bell System)
the spacing signal, the input of transformer T2 is short-circuited at the step-up transformer,
and no carrier current reaches the line. The receiving relay is operated to spacing (4),
when no current is being received from the line. The 0.2-megohm resistance inserted in
series with the line winding of transformer TI assists in reducing the carrier to the line
and lessening the load on the carrier supply during spacing in this system. The send and
receive filters pass only the carrier frequency assigned to the particular channel with
which they are associated.
The telegraph level at a given point on the circuit is the power at that point due to a
single steadily marking channel and is expressed in decibels referred to 1 milliwatt (dbm).
If frequency distortion is present, the level refers to a channel operating at or near 1000
cycles, which is the nominal telegraph level. The telegraph levels on the line section of a
circuit, in general, must be high enough to override line interference and low enough to
prevent modulation and crowding, which introduce objectionable interference in other
systems. The sending and receiving levels in the same telegraph system should be such
that cross-induction will not occur between the sending and receiving branches in ihe
terminal cabling and equipment.
Specific telegraph level (STL) of a circuit used alternately for telephone service is
numerically equal to the power of one telegraph channel (in dbm) at a point of zero tele-
phone transmission level. At present in the Bell System, this level is — 16 db for type C
carrier (except in certain cases) and — 21 db for other telephone facilities. The proper
selection of the STL in any given case is highly important in the application of telegraph
to telephone circuits, because of the dependency of the satisfactory operation of both
services, when related, on this factor.
The telegraph signaling spaed that can be obtained on a carrier channel depends on the
band width or frequency range of the channel. With wider bands, higher signaling speeds
per channel are possible but fewer channels are obtained. When the carrier channels are
spaced 170 cycles apart, each channel will allow telegraph signaling at speeds of 35 to 40
cycles per second, which permits of the operation of a three-channel multiplex working at
50 words per minute per multiplex channel. Thus, a twelve-channel carrier system oper-
ated in this way would have a total capacity of 1800 words per minute in each direction
simultaneously. With 300-cycle spacing between carrier channels, telegraph speeds as
18-36 TELEGRAPHY
high as 75 cycles per second may be obtained on each channel, which permits the operation
of a four-channel multiplex at 75 words per minute per multiplex channel. An eight-
channel system of this type has a capacity of 2400 words per minute in each direction
simultaneously.
Voice-frequency carrier systems are usually operated over four-wire circuits, one pair
being used for the channels working in one direction and the remaining pair for channels
working in the opposite direction. They may be operated on two-wire circuits, however,
by transmitting the lower half of the carrier frequencies in one direction and the upper
half in the opposite direction in a manner similar to the high-frequency carrier, which is
described in this article.
Standard voice or carrier telephone repeaters are employed for voice-frequency carrier
telegraph systems assigned to voice or carrier telephone facilities. These repeaters take
the same spacing as would be employed if the facilities were assigned to telephone circuits.
Carrier supply for the different carrier telegraph frequencies in the type of system
shown in Fig. 21 is now generally furnished by vacuum-tube oscillators, although some
motor-driven multifrequency generator sets are still in service. One vacuum-tube oscil-
lator unit has a capacity for as many as 50 carrier telegraph channels normally but for a
short time may supply a much greater number of channels. Harmonic control is provided
for the vacuum-tube oscillator supply to limit high peak line currents, which would tend
to overload the telephone repeaters and, in carrier systems, cause interchannel inter-
ference.
Voice-frequency carrier transmission is sometimes employed between a teletypewriter
office and an outlying teletypewriter station, particularly where a d-c telegraph channel
cannot be satisfactorily provided.
In this system, a carrier frequency of 690 cycles transmitting from the office and 1640
cycles transmitting from the station is used. Carrier current is transmitted for spacing
and no current is transmitted for marking signals. The break relay at the office can thus
be omitted, since the sending relay opens the receiving circuit during transmission of a
spacing signal, which holds the receiving relay on its marking contact. Also carrier
current is not sent over the line from either terminal while the receiving circuit at that
terminal is connected to the line.
Filters are required at both terminals, in order to prevent echo current effects from
reaching the detectors and causing false signals.
The series resistance across the low-pass filter at the station provides for spacing signal
feedback to the station amplifier detector circuit and permits obtaining a home copy of
the outgoing-station message.
The operation of this carrier system does not affect the usual telephone circuit trans-
mission over the line and is not materially affected by reasonable amounts of line leakage
or by earth potentials, crossfire, or power induction in the circuit.
High-frequency carrier telegraph systems for open-wire application have been employed
by the larger communication companies for a number of years. The ten-channel open-
wire systems of the Bell companies are no longer standard, owing to the improvements
and economies secured from the eighteen-channel voice-frequency system described above.
The Western Union Telegraph Co. has developed a series of carrier telegraph systems
specially designed to fill the requirements of the domestic telegraph system. A number
of these systems are in operation (1947), and additional systems are being installed rapidly
in a modernization program in which carrier operation will replace d-c telegraph opera-
tion for trunk circuits and will substantially reduce the number of wires and pole lines
required for the telegraph service. These systems include (1) a portable type for estab-
lishing short temporary or emergency channels, (2) a low-cost four-channel system for
distances not greater than two repeater sections, and (3) four types of multichannel,
long-distance trunk systems. The basic, standard unit of the trunk carrier systems is a
3000-cycle voice-frequency band extending from 300 to 3300 cycles. The four trunk
systems are (1) the 7.5-kc type E with one voice-frequency band in each direction, (2) the
15-kc type F with two bands in each direction, (3) the 30-kc type G with four bands in
each direction, and (4) the type WN with 32 bands in each direction and requiring a
transmission band of 150 kc in each direction. Types E, F, and G are open-wire systems
designed for two-wire operation and with frequency allocations (for 300-cycle channels)
as shown in Fig. 22. The type WN is designed for use with a two-way microwave radio
relay circuit.
In^multiband systems, only one band can be transmitted in its original frequancy
position (300 to 3300 cycles) ; all other bands must be transferred or translated to separate
positions hi the available frequency spectrum of the transmission medium. This can be
accomplished by modulating each of the bands requiring translation by a separate second-
ary carrier of appropriate frequency. Such a method is wasteful of the frequency spec-
ALTEKNATING-CTJRRENT TELEGRAPH SYSTEMS 18-37
trum because of the increasing inefficiency (in absolute band width) of selective filters as
the frequency is increased. The Western Union systems utilize the spectrum more effi-
ciently by employing a plural or tandem method of modulation in which the voice-fre-
, quency bands are translated in groups, thus requiring only broad group niters at the
assigned position in the frequency spectrum. The secondary carrier or translation fre-
quencies are supplied by amplified harmonics of a high-stability, low-frequency oscillator.
Although these carrier systems are designed primarily for operation over Western Union
facilities, they are readily adapted to operation on any wire or radio transmission system
that provides a suitable transmission band. Furthermore, the individual voice-frequency
bands can be repeated or patched at will between the four types of Western Union multi-
band systems, Bell System facilities, and equivalent facilities of other companies.
The voice-frequency bands may be utilized for high-speed facsimile telegraph trans-
mission or for operation as a telephone circuit, but they are ordinarily channelised for
E SYSTEM
F SYSTEM
68 0246
Frequency in kilocycles
Q SYSTEM
8 10 12 14 16 18 20
\
|
«
1
/
ja
"?
>
\\
t
/
taJ
ttc
>vJ
est
We^
1 1
3 t
psj
i
/
/
j
.
/j
I 10
&
3ar
d /
MUs
me
B
Ba
id
D
eJ
nd
c
/
1
B
3tK
ic
i
Bar1
d 0
\
3an
d I
JandJ
k
•
^
u
JUU
1U
Mill
IU
U
fl
UJi
U
W
Ul
m
w
/
ul
uJ
ut
'I
uu
Jit
t/
i
W
i.U
Ul
UW
™»
U
•
/
^A
^
J
^.
'_^x
x
°0 2 4 6 f 8 10
12
14
16 18 20 22 j24
Frequency in kilocycles J
26
2S 30 i 32 34 3€
6.86 K.C. carrier 114.06 K.C-. carrier
and
23.66 K.C. pilot 80.86 K-C. carrier
channej
pilot channel
„ ocations for ' „.._., .
Union Telegraph Co., A.I.E.E., F. E. D'Humy, and P. J. Howe)
FIG. 22. Frequency Allocations for Three Types of ^Carrier Telegraph Systems ^(Courtesy Western
"" ' .E.E., F. " T^' T T-W T TT
printer or other code telegraph operation. Two types of channelization are employed,
providing (1) nine-wide-band channels spaced 300 cycles apart and suitable for four-
channel multiplex operation at speeds up to 75 cycles per second, and (2) eighteen, narrow-
band channels spaced 150 cycles apart and suitable for teleprinter or two-channel multi-
plex operation. Present trends are away from the relative mechanical complexity of
multiplex telegraphy and toward teleprinter operation; consequently, narrow-band
channels only are now being installed.
The following description deals with narrow-band channels, but it also applies gen-
erally to the basically similar wide-band equipment. The sending terminal of each chan-
nel includes a vacuum-tube oscillator, which supplies the channel carrier frequency. The
d-c telegraph signals are impressed or superposed on the carrier by modulation. The
carrier telegraph systems of other companies use amplitude modulation, as did the early
Western Union systems. For amplitude-modulated (a-m) operation, the channel carrier
frequency is transmitted for a marking signal and interrupted for a spacing signal. West-
ern Union has introduced, and now uses exclusively, frequency modulation for carrier
telegraph transmission. In f-m transmission, the frequency of the channel oscillator is
controlled by the d-c telegraph signals being transmitted. Marking and spacing signals
cause the frequency to swing down and up, respectively, 35 cycles from midchannel fre-
quency. The transitions between marking and spacing frequencies are not instantaneous
but are very abrupt, with the frequency increasing and decreasing smoothly between the
lower and upper limits. This action results in true frequency modulation, and the modu-
lated carrier current appears at the output of the channel transmitting filter constant in
amplitude but varying in frequency.
At the distant corresponding channel terminal, the carrier is selected by the receiving
filter and amplified, after which it passes through an amplifier limiter, a frequency dis-
criminator, and a rectifier circuit, which restores the marking and spacing frequencies to
18-38 TELEGRAPHY
their original d-c form. The vacuum-tube limiter circuit maintains a constant-amplitude
output for received levels in a range between —50 and +10 dbm.
In comparison with a-m transmission, f-m transmission is definitely less susceptible to
interference, and the received signals are immune to the influence of level variations en-
countered in transmission.
The original f-m channel terminals contained transmitting and receiving relays. In
the latest type of narrow-band equipment, the relays have been eliminated and operation
of the channel terminals is completely electronic. This change, together with other
simplifications, has effected a considerable reduction in size and cost of equipment.
Transmission losses in the open-wire systems between sending and receiving terminals
are compensated for by vacuum-tube repeaters, spaced at suitable intervals along the
line. Average wet-weather losses are limited to about 25 db between repeaters. Reflec-
tion losses at junctions of open wire and incidental intermediate or terminal cables are
limited by impedance-matching networks. Loading of short cables to reduce attenuation
losses is no longer favored. Networks are provided at repeaters and terminals to equalize
the losses at different frequencies, so that the attenuation is substantially uniform over
the carrier band.
Telegraph circuits can be operated across the United States entirely by carrier without
requiring a regenerative repeater at any point. The type G system provides, in each
direction, on a single pair of wires 72 teleprinter circuits or 144 multiplex channels having
a total capacity of 4750 and 9500 words per minute, respectively, in each direction. The
other systems provide capacities proportionate to the number of voice-frequency bands
employed. The radio relay system with its 576 carrier channels handles 38,000 words
per minute each way.
9. FACSIMILE SYSTEM
Facsimile, as defined and discussed in detail elsewhere in this handbook, is a process
whereby such objects as a picture or a sheet of paper containing printing or writing are
electrically scanned, and the electrical currents thus generated are transmitted by wire or
radio to a receiving device which reproduces, as a print or on a specially prepared paper,
the original picture (in black and white) or the printing or writing. The following brief
discussion applies to facsimile as used in telegraph operation only.
Facsimile transmission of messages, as employed by the Western Union Telegraph Co.,
is known as telefax service or transmission. This type of service was considered desirable
by the telegraph companies for many years, but the recording systems used, employing
photographic, chemical, or other processes, were too costly or slow for the general handling
of telegrams.
In recent years, the Western Union Telegraph Co. developed for its use a facsimile
recording paper, with the trademark Teledeltos. This paper has a conducting coating of
a light gray color which is marked in black by the passage of an electric current through
it. The paper is used dry, requires no processing, is not affected by light or ordinary
moisture conditions, and produces immediately a clear-cut permanent record. Simple
Telefax recording equipment receives the incoming amplified facsimile currents and
applies them directly to the paper by means of a stylus riding on the surface of the paper.
The Telefax equipment thus far developed is of several different types and has been
designed primarily to provide maximum convenience for the general public. However,
trunk-line Telefax is being used to some extent between large centers, as between Chicago
and New York. These trunk circuits have been used mainly for the transmission of
drawings, sketches, copy for publication, editorial corrections, and commercial messages.
For good-quality Telefax transmission, a frequency band width of about 2500 cycles is
required. The line loss at the maximum frequency used should not exceed about 25 db.
10. MISCELLANEOUS TRANSMITTING AND SIGNALING SYSTEMS
The ticker system is designed to furnish stock, bond, and grain quotations and pertinent
news items to brokerage, investment, and private offices during trading hours.
The ticker, which does not include a transmitting keyboard, is otherwise quite similar
in principle to the start-stop printer, the chief points of difference being in the form of
type wheel used and the method employed in shifting from letters to figures. An eight-
unit code is used. The first impulse of each group starts the printer; the second impulse
determines by its polarity whether letters or figures are to be printed; the succeeding five
pulses determine the particular character to be printed; and the eighth pulse is the stop
pulse, which allows the distributing mechanism to come to rest in preparation for the
MISCELLANEOUS SIGNALING SYSTEMS
18-39
next succeeding signal group. The tickers are controlled by a single transmitter at the
central distributing point. Normal operating speed is from 450 to 500 printed characters
per minute.
The teleautograph system is employed principally by banks, railroads, department
stores, and similar businesses. This system provides a means by which messages, written
in longhand at one station, may be reproduced simultaneously at one or more stations at
various locations without material distortion of the original characters.
^ The principle on which this system operates is shown in Fig. 23. The transmitter con-
sists of a stylus, which is mechanically connected, through two sets of levers and appro-
priate swivel joints, to the contact arms of two variable rheostats in such a way that the
horizontal and vertical components of the stylus movements are translated into cor-
responding current variations in two lines connecting the receiver. At the receiver, the
variations in the line currents produce similar movements in two coils or "buckets"
within a magnetic field. The movements of these coils are communicated through a
system of levers to a writing pen which reproduces the movements of the sending stylus.
[ Relay" Paper Shifter Vlb. (p L) Reh
L 1 S.gn.lBuzz.r/ / ^.^
Transmitter
FIG. 23. Schematic Diagram of the Telautograph System
The pen is lifted from the paper and the paper is shifted to provide fresh writing surface
by magnets, which are controlled by superposed alternating current supplied by a buzzer
located in the transmitter.
Two grounded circuits are required, one to transmit the current variations representing
each of the two components of the stylus motion. As many as 100 receivers, arranged to
be controlled by one or more transmitters, may be operated in multiple on a pair of wires.
The speed of operation is determined entirely by the rapidity with which the operator
can write. The line potential is usually 120 volts with one side grounded, and current
depends upon the resistances of transmitters and receivers. One type of equipment,
which normally operates on 100 ma, is adapted for use on wires not exceeding 700 ohms
resistance each. Another type requires only 60-ma line current and will operate well on
lines up to 1200 ohms resistance, although in a few extreme cases operation has been
maintained on lines having resistances as high as 1800 ohms.
Messenger call circuits are employed for summoning telegraph messengers to pick up
messages at various locations and deliver them to the telegraph office for sending.
Signals are transmitted by a call box, which consists of a spring-driven clockwork
mechanism arranged to turn a pair of notched contact wheels through one complete revo-
lution each time the box is operated by turning and releasing a winding key, as shown in
Fig. 24. The contact wheels are arranged both to open and ground the line when trans-
mitting signals, and to restore the line to its normal closed ungrounded condition upon
coming to rest. The call boxes are connected in series with a line having both ends ter-
minated at the central office in relays which operate a buzzer and a register for recording
the signals on a paper tape. Switches Si, &, and S$ are provided to change the line,
battery, and register connections to permit of receiving signals from the call boxes even
during times when the line circuit may be accidentally open or grounded or both. Only
the simultaneous occurrence of a fault on both sides of a call box or group of boxes will
prevent the transmission and correct reception of signals. The normal line current in
call circuits is 50 ma, and, for satisfactory service, not more than 50 call boxes should be
included in any one circuit. Signaling speed usually does not exceed 4 impulses or 2
cycles per second.
18-40
TELEGRAPHY
Though many technical advances have been made in the art of telegraphy, the mes-
senger call box, of which there are over 300,000 in the United States in offices, hotels, and
other public places, still plays an important part in the collection of commercial telegraph
messages.
FIG. 24. Schematic Diagram of a Messenger Call Circuit
Clock circuits are employed in furnishing telegraph time service. The clocks at sub-
scriber premises are driven by springs which are wound periodically, usually once each
hour, by a small electric motor operating on dry batteries. The minute and second hands
are arranged so that they may be moved to their 12 and 60 positions, respectively, by the
operation of a synchronizing magnet. The synchronizing magnets of the clocks are con-
nected in series in a grounded circuit terminating at the central office on the contacts of a
transmitting relay or a synchronizing machine which sends a synchronizing impulse 1 sec
long once every hour, in response to the operation of contacts of a master dock. The
transmitting circuit is arranged to give an audible signal if the synchronizing impulse fails
to be transmitted owing to line failure. The clocks mechanically lock their synchronizing
mechanisms in the inoperative position except for two or three minutes immediately
preceding and following the time at which the synchronizing impulse is to be received, so
as to protect the clocks from being set to a false position by accidental crosses between
the line and power circuits. The normal line current is 250 ma, and approximately 60
clocks may be operated on one circuit.
Naval Observatory time signals are regularly distributed to all parts of the United
States by the Western Union Telegraph Co. over about 200,000 miles of wire network.
These signals provide the means for maintaining some 2000 master clocks, so that they
continuously indicate time to a practical degree of accuracy.
Railroad communication systems employ the latest types of telegraph as well as tele-
phone and radio facilities for the control of train movements and the general business of
the railroads. The telegraph facilities used are, in general, similar to those previously dis-
cussed in this section and will not be considered further here. Special arrangements of
telegraph facilities are employed by the railroads to meet their special needs.
SUBMARINE CABLE TELEGRAPHY
By John D. Taylor
Submarine cables interconnect all the earth's continents for the transmission of tele-
graph messages.
One large telegraph company has more than 30,000 miles of ocean cable, some of it lying
at a depth of nearly 3 miles. This company laid its first cable in 1873 and its latest cable
in 1928. The North Atlantic is spanned by 14 cables, and 6 cables extend between North
America and the Azores, where connections are made with Europe and, via the Cape
Verde Islands, with Africa and South America. There are other cables between the
United States and Mexico, South America, and the West Indies. Three cables span the
Pacific Ocean.
CABLE DATA
18-41
11. CABLE DATA
The first transoceanic cables laid were of the non-loaded type. It was not until 1924
that the first loaded cable was placed, and this cable connected New York with Horta,
Azores Islands.
Non-loaded cables of the deep-sea type usually consist of a single copper conductor,
which may be solid, stranded, or a combination of both, to provide greater flexibility, as
shown in Fig. 1. This conduc-
tor is encased in gutta-percha *
insulation, covered with servings
of jute yarn over which steel
armor wire sheathing is placed
to provide mechanical strength
and protection. The armor wires
are covered with inverse layers
of jute over which an outer
covering of compound is applied. The overall diameter of deep-sea cable varies from about
3/4 in. to 1 1/2 in., depending on the size of conductor and the construction employed.
Table 1 shows certain properties of non-loaded cables now in operation.
Table 1. Certain Properties of Non-loaded Beep-sea Cables
PIG. 1. Non-loaded Submarine Cable Construction
Weight, pounds per
Diameter
Diameter
Resistance,
Capacitance,
nautical mile
of
over
ohms per
microfarads
Copper
Gutta-percha
Conductor,
mils
Gutta-percha,
mils
nautical mile
at 75 deg fahr
per nautical
mile
70
120
70
252
16.90
0.272
107
120
86
258
11.05
0.316
107
166
86
298
11.05
0.280
130
130
95
270
9.10
0.334
140
140
99
280
8.45
0.335
160
150
106
291
7.40
0.345
180
160
112
302
6.58
0.351
200
180
114
318
5.92
0.339
225
225
124
354
5.25
0.332
275
225
138
360
4.30
0,363
350
300
151
412
3.38
0.347
500
315
180
432
2.37
0.398
650
400
203
487
1.82
0.398
700
360
211
470
1.69
0.435
The shore ends of ocean cables are usually of the twin-conductor type, a cross-section
of which is shown in Fig. 2. The second conductor in the end cable is used to extend
the circuit ground terminations out into deep water for the purpose of minimizing extra-
Deep Sea
Conductor
Shoce i3rnH
Dotfele Yarn Serving an
PeraaaOoyTa
Copper Tap«s
Copper
Wire
FIG. 2. Loaded Deep-sea Cable Construction
neous ground disturbances from power circuits and natural causes. Since the end sections
of cable usually rest in shallow water and are subject to severe water action and other
* Deproteinized rubber has been employed as a substitute for gutta-percha, and a synthetic
insulation of polyethylene is being experimented with.
18-42
TELEGKAPHY
disturbances near shore, the construction is much heavier than for the deep-sea sections,
both in armoring and jute layers, so that the overall diameter may be as large as 4 in.
Loaded cables, in their make-up, closely resemble the non-loaded cables just described,
the principal difference being that the copper conductor or conductors (for twin conductor)
are spirally wrapped with a thin, high-permeability tape of Permalloy (alloy of nickel
and iron) (see Fig. 2) . This tape uniformly and continuously loads the copper conductors
and results in material signal transmission improvements (over the non-loaded cable),
such as lower and more uniform attenuation with frequency and less distortion.
Table 2 shows certain properties of loaded cable now in service.
Table 2. Certain Properties of Loaded Deep-sea Cables
Weight, pounds per
nautical mile
Diameter in
Mils-over
Resistance,
ohms per
nautical mile
at 75 deg fahr
Capacitance,
microfarads
per nautical
mile
Inductance,
millihenries
per nautical
mile
Copper
Gutta-
percha
Loading
Material
Con-
ductor
Load-
ing
Gutta-
percha
573
517
255
277*
605 *
387
355
252
258
370
72
61
43
73
104
180
171
121
126
182
192
182
132
148
202
480
430
360
375
2.09
2.31
4.65
4,28
1.97
0.370
0.375
0.318
0.340
0.393
63
86
140
170
118
* Approximate values.
12. OPERATION
Long non-loaded submarine cables (the longest being about 3500 nautical miles) have
high values of resistance and capacitance, which attenuate and distort the telegraph sig-
nals to such an extent that, until recently, the usual methods of land line operation could
not be employed.
Early methods of transmission employed a modified form of bridge duplex with artificial
line, giving duplex operation, and electromechanical types of receiving equipment.
Signals were transmitted in the cable Morse Code from a perforated tape by a trans-
mitter and a group of associated relays, arranged to apply positive or negative battery
or ground to the apex of the bridge circuit of the duplex set in accordance with the code.
The receiving instrument first used on transatlantic cables was a moving-coil-type
mirror galvanometer, connected as such in the bridge duplex circuit. Because of its
sensitivity and favorable signal-shaping characteristics, this instrument was used for
many years, until replaced by the siphon recorder, which recorded on a moving paper
tape in ink the variations in magnitude of the incoming signals. The recorder was later
supplemented by (1) various types of magnifiers, which amplified the received signals
before the signals reached the recorder, and (2) sensitive cable relays, such as the drum
and gold-wire types, which permitted dispensing with manual relay operation at repeater
stations.
These developments, together with the application of regenerative repeaters, extending
to the period immediately after World War I, made possible greater signaling speeds, but
with recorder operation it was still necessary to transcribe messages manually from the
recorder tape at the receiving terminal. Satisfactory operation required that the unbal-
ance current in the receiving arm of the bridge should not exceed one-sixth the value of
the received signaling currents, thus necessitating the maintaining of a duplex balance
between the cable and artificial line within about 1/100 per cent.
Because of the high cost of submarine cables, intensive study and experimental work
have been continuous, new techniques and devices being sought for increasing the effi-
ciency of these cables. The electromechanical receiving equipment was necessarily
fragile to respond to weak signals, and the gain of the magnifiers was relatively low as
compared to electronic amplifiers. Attempts in 1918-1919, to apply vacuum-tube signal-
shaping amplifiers to improve signal reception did not result favorably, mainly because
of (1) high level disturbances existing at that time on duplexed non-loaded cables, due to
interference and duplex unbalances, and (2) the fact that suitable electrical networks,
equivalent to or better than the mechanically tuned moving coil, were not available.
With the laying of the first loaded oceanic cable in 1924, higher signaling cable speeds
were possible, limited by recorder operation and other terminal equipment. Concentrated
effort toward improving this equipment resulted in the development of a signal-shaping
amplifier and a multiplex printer system suitable for high-speed loaded-cable operation.
This equipment was installed on the first and subsequent loaded cables, resulting in rais-
OPERATION
18-43
ing the message capacity of these cables as much as three to eight times over that of the
older, non-loaded systems. These loaded systems are still giving satisfactory service.
The substantial gams made in cable message transmission through development of the
loaded-cable system called forth increased effort toward bettering the non-loaded cable
performance. The results so far attained have been successfully applied quite extensively
in the North Atlantic and in the Alaska communications cable systems, having been
accelerated by the needs of World War II.
The improvement program in non-loaded submarine cable operation has included (1)
conversion from cable code recorder operation to five-unit code printer operation, (2)
replacement of magnifiers with vacuum-tube signal-shaping amplifiers which permit the
use of rugged land-line-type polar
relays, and (3) improvements hi
duplex artificial line networks and
in the technique of balancing.
Thus, the advantages of more
nearly automatic operation, in-
creased circuit speeds, and reduced
maintenance at cable stations have
been secured.
The printer system standardized
for non-loaded cables is funda-
mentally similar to the loaded-
cable system but more nearly re-
sembles the land line multiplex. _ ^ _ . ^
T± ™«l™c. -,-,0/v rt-p •*-'k« +0-^^ 4- ««,-,»«*+ ^IG- 3. Typical Arrangement of Terminal tmts for Du-
It makes use of the tape transmit- plexed NonlYoaded Cabfe (Courtesy Western Union Tde-
ter, rotary distributor, synehroniz- graph Co., A.LEJE., and C. H. Cramer)
ing mechanisms, and printers, thus
providing for integrated operation with land line systems. It differs from these latter
systems in that it is applied to single as well as multichannel operation, whereas the land
line system requires start-stop seven-unit code printers for single-channel use; and on
long cables the printer signals are transmitted at a speed such that pulses of unit or dot
length are received at very small amplitude and, in effect, are considered as absent.
The receiving networks are adjusted to respond to signals two or more units long, so
that, from the standpoint of signal reception, the fundamental received frequency is one-
half the transmitted dot frequency. The receiving relay operates on a three-position
basis, remaining at the zero position for dot signals, which are reinserted synchronously
by the receiving rotary distributor. The at-
tenuated-dot method of transmission, though
appearing to permit doubling the cable output
as compared with normal multiplex trans-
mission, only approaches such output as a
limit. Actually, the increase in letters-per-
minute circuit speed is only about 80 per cent
over that attainable with, normal transmis-
sion, because, with attenuated-dot transmis-
sion, the received signals are more susceptible
to interference and more difficult to shape.
With this method, the five-unit code used in
land line multiplex functions as a 2.5-unit code,
giving a net gain over the 3.7-unit recorder
Morse code.
The cable printer system is flexible in
that individual channels may be terminated,
extended, or combined with other channels
to satisfy traffic requirements and the trans-
Channel efficiency may be increased by the a^ppli-
Resonant-frequency
cycles per Second
17.5
J- 2.16 MH
FIG. 4. Typical Arrangement of Resonant
Balance Networks (Courtesy Western Union
Telegraph Co., A.I.E.E., and C. H. Cramer)
mission speeds of the available circuits,
cation of land line automatic systems.
Figure 3 shows a typical arrangement of important terminal units for duplexed non-
loaded cable, including a pre-amplifier shaping network, an amplifier tinit, receiving relays,
and a local correction network. Resonant balance networks, as shown in Fig. 4, are also
provided in a balanced arrangement between the series condensers and the bridge points of
the receiving circuit.
The pre-amplifier shaping network, shown diagrammatically in Fig. 5, has been designed
to meet certain requirements which permit satisfactory printer operation on long non-
loaded cables at the highest practicable speeds, the more important being:
18-44
TELEGRAPHY
Input to
amplifier
1. A higher standard of receiving accuracy, continuity, and reliability of operation
than with recorder operation.
2. The ability to equalize or restore the received frequency components of the signals
to an approximation of the original amplitude and phase relationships.
3. Passing only the narrowest band of frequencies, consistent with avoiding undue
characteristic distortion and with limiting the effects of extraneous interference and
duplex unbalance voltages. Direct cm-rents and alternating currents of near-zero fre-
quency must be rejected, in order
L°fTite8r?S resonant to avoid effects from earth currents,
particularly as a result of magnetic
storms.
4. A shaping network electrically
symmetrical with respect to the
duplex bridge or electrically isolated
from the bridge.
5. Network elements designed for
a wide range of adjustment.
6. Amplifier gain and output suf-
ficient to operate rugged polar re-
lays, similar to those used in land
line systems.
This pre-amphfier network, when
P^rly adjusted passes a band
of frequencies, including those com-
ponents required for good signal shape, properly proportioned and phased, and largely
or almost completely suppresses those frequencies below the fundamental received fre-
quency. The first branch of the network, being symmetrical and directly across the
duplex bridge, is tuned to about 1.5 times the received frequency. The remaining ele-
ments of the network, being isolated from the bridge by shielded transformers, are
arranged in two paths which combine at the amplifier input.
The lower frequencies pass to the amplifier over the low-frequency path with little, if
any, further shaping, while the higher frequencies pass to the amplifier over the high-
frequency path, in which they are further shaped by a bridge-type phase-adjusting net-
work, a low-pass filter for added suppression above the required signal band, a parallel
resonant circuit tuned to 1.5 times
the received frequency, and suit-
able resistance controls. The
phase-adjustment network pro-
vides the required wave-front
steepness with less higher-fre-
quency components, thus permit-
ting further discrimination against
unwanted frequencies.
The amplifier unit is of the
three-stage resistance-capacitance
coupled, pushpull type with two
stages of voltage amplification.
Frequencies below those received
from the shaping network are sup-
pressed. The maximum voltage
gains and available overall gains
are 83 db and 103 db, respectively.
The amplifier output is adequate
B
Tims
FIG. 6. Received Signal Resulting from Transmission of
Long Signal over Non-loaded Submarine Cable (Courtesy
Western Union Telegraph Co., A.IJE.E., and C. H. Cramer)
A. Component through high-frequency path of Fig. 5.
5. Component through low-frequency path of Fig. 5.
C. A + B.
D. Component supplied by local correction network.
- . , , , , , , j , . E. Complete signal, C + D.
for operating the latest land-line-
type polar relays.
Two standard two-position re-
lays function in unison as a three-
position relay, in accordance with usual cable practice, but the circuit is readily converti-
ble, if desired, to receive two-current signals.
Figure 6 shows the shapes of the component signals in the formative stages and the
shape of the complete signal at the amplifier input. Curve C shows the signal shape as it
leaves the pre-amplifier network, at which point signals of the fundamental received fre-
quency are fully shaped but longer signals would be badly distorted because of lack of
low-frequency components. The local correction network (Fig. 3) functions to restore
these components under control of the receiving relays. The shaped local correction
OPEEATION
18-45
voltages, curve Z>, are added to the received signal in the grid circuit of the output stage
of the amplifier, resulting in the fully shaped and complete signal, curve E.
For loaded-cable systems, essentially all signal shaping occurs in the pre-amplifier and
interstage networks, but there is some deficiency in the very low-frequency components.
The method of shaping employed with the non-loaded cable systems not only affords
greater immunity from low-frequency disturbances but simplifies amplifier design and
stability and eliminates slow transients (wandering zeros) .
Duplex operation of non-loaded cables, giving greater total message capacity, is nor-
mally used. With the advent of modern amplifiers, extraneous interference and duplex
unbalance levels limit signaling speeds. If un-
balance is governing, maximum capacity is ob-
tained by using unequal speeds in the two direc-
tions of transmission, but duplex unbalance is
at present less of a factor, owing to improved
artificial lines and balancing methods.
The basic ocean cable artificial line is still
about the same as it was at the beginning of
duplex operation. The lumped series resist-
ances and shunt capacitances, simulating cor-
responding cable constants, have been subdi-
vided and arranged for greater flexibility of
adjustment. Modern artificial lines of Ameri-
can design are subdivided so that the lumped
values of resistance and capacity increase pro-
gressively as their distance from the head
(point nearest the apex) of the artificial line
increases.
The cable circuit parameters include induct-
ance and effective resistance, which vary with
frequency because of the earth-return path
characteristics, and are known as the sea-return
impedance. These factors, though small, are
important in high-accuracy balancing of the
near end of the cable. By using tapered re-
sistance values in series with the shunt capac-
itance elements of the artificial line sections,
the sea-return impedance can be simulated
over a relatively wide frequency band and the
propagation constant of the sections to which
these resistances are added is not materially
changed.
However, in order to meet balance require-
ments, further refinements in duplex balanc-
ing are necessary. Slow reversals are trans-
mitted, and observations of the residual unbal-
.8
.7
.6
.5
.4
.3
1*
I'1
§ 0
3
§ .1
I-2
0) <a
0£ -3
.4
.5
.6
.7
.8
.9
/
1
JO
(
V
A-V
:§
/
.2
A
s
/ 4
ctance
/ /
_^ ^
" A
x\^
^^
v-x/
V
\
\
%x\*-i
3~\/
S
\
v
.,""' ^
0
A
A
/
£
\
Resi«
tance
CO
\
/
s
\
) 10-20 30 40 5C
Frequency-cycles per second
A. Before insertion of networks of Fig. 4.
B. After insertion of networks of Fig. 4.
FIG. 7. Frequency Characteristic of Unbalance
on a Transatlantic Cable (Courtesy Western
Union Telegraph Co., A.I.E.E., and C. H.
Cramer)
ance transient are made with a cathode-ray oscillograph or ink recorder. In the final
adjustments, unbalance at operating speeds is also observed. The artificial line adjust-
ments have their limitations (which are not usually the same for different cables), because
of inadequacy of artificial line, interferences, or other factors.
Corrective resonant networks are designed to secure the ultimate duplex balance needed
for satisfactory operation. These networks, Fig. 4, supplement the artificial line and
provide an impedance, which can be effectively controlled as to magnitude and width of
frequency band. The networks are designed in accordance with a frequency character-
istic of the residual unbalance.
This frequency characteristic is obtained by taking electrical measurements, directly
across the duplex bridge over the important frequency range, of the effective residual
impedance unbalance at the head of the artificial line. Several of the single networks are
usually used, some of them being inserted in series with the cable and some of them in
series with the artificial line and adjusted, as required. Final adjustment is made in the
usual artificial line controls.
Figure 7 shows the frequency characteristic of unbalance on a transatlantic cable before
and after insertion of the corrective resonant networks and the final adjustments. The
balance has been improved by these networks over the most important frequency band,
with the greatest improvement at the higher frequencies.
18-46 TELEGRAPHY
Crossfire between cables usually occurs if two or more cables land at the same point and
extend underground to the cable station with small separation. This interference is con-
trolled by applying simple corrective networks at the cable station. If two cables land
at different points and are laid closely parallel for some distance, the corrective problem is
more difficult, requiring more complex networks.
With the techniques that have been developed for improved duplex balances and the
correction of crossfire, extraneous interference, mostly of natural origin, becomes con-
trolling in signal speed. Natural interference is picked up in the shallow-water end sec-
tions of cables, its magnitude varying widely from cable to cable, depending on the depths
and distances encountered. Receiving earths of the non-loaded cables are usually located
up to several miles from shore. The twin-conductor end sections of cable greatly assist in
limiting the interference and could be extended further into the ocean, but the cost would
be correspondingly increased.
Some improvement in interference levels has been obtained by increasing the sending
voltages, restricted until recent years to about 50 volts, up to 90 to 120 volts, now in com-
mon use by some of the cable companies.
Signal-shaping amplifiers of the type just described are being used on many of the longer
transoceanic cables; short-cable amplifiers are employed for short connecting cables.
On certain duplex-operated non-loaded cables, the sum of the letters-per-minute speeds
in the two directions now averages in printer operation over 40 per cent more than with
the previous recorder speeds. The average net increase in the message capacity of these
cables, considering short-cut methods permissible in recorder but not printer operation, is
over 30 per cent. In one case, it is expected that the ultimate speed in printer operation
when three-channel multiplex equipment is available will be 750 letters per minute in
each direction of transmission.
In loaded cables, the channel speed is usually 250 to 300 letters per minute, the number
of channels per cable varying between 4 and 8, depending on the cable make-up. One
loaded cable, about 2300 nautical miles long, operates at 65 cycles per second and provides
5 one-way channels, each with a capacity of 312 letters per minute.
Power equipment consists of storage batteries and charging-equipment installations of
the capacities and sizes necessary to provide both regular and emergency power at the
cable stations. The d-c voltages range from 90 to 120 volts.
TELEGRAPH EQUIPMENT
By John D. Taylor
The telegraph central office is the centralizing point which, for its particular area,
directs and regulates the movement of telegraph messages. From such points, the operat-
ing personnel also maintains constant supervision over the proper functioning of and
needed repairs to equipment and outside plant.
13. CENTRAL-OFFICE EQUIPMENT
Central-office equipment for telegraph operation consists of a wide variety of equip-
ment units and associated facilities. The types and amounts of equipment at any given
central office vary over a wide range, depending mainly upon its importance in the general
telegraph network, the message volume handled, and the nature of the traffic. Some of
this equipment has previously been described and will not be discussed further here.
In a large office, the principal classifications of equipment may be considered to include:
1. Terminal equipment for open-wire lines — entrance cables, protector and distributing
frames, and test board (Western Union designation is line-terminal switchboard) .
2. Intermediate operating equipment — repeaters, concentrators, and system apparatus,
such as multiplex, varioplex, reperforator-switching, carrier, and Telefax.
3. Operating positions — teletypewriter switchboard (Bell System designation), operat-
ing tables or positions for Morse, multiplex, and teleprinter sending and receiving appa-
ratus, tape perforators, reperforators and transmitters, Telefax terminals, telephone lines,
and switching facilities.
4. Message-handling equipment — belt conveyors between incoming and outgoing operat-
ing positions and distributing centers within an office, and pneumatic-tube terminals
from branch or other message-handling centers to the main office.
CENTRAL-OFFICE EQUIPMENT 18-47
5. Power equipment — power-generating equipment, such as rectifiers and motor-genera-
tors, power switchboards, power distributing systems to power-operated units, storage
batteries, and emergency power plants.
6. Building equipment — lighting, heating, ventilation, elevator service, personnel
quarters, and many other items of this nature.
The equipment layout in an office should provide a minimum travel time of the operat-
ing personnel in their regular work and should limit wiring and cabling requirements be-
tween equipment units.
Protector (main) frames provide for termination of the entrance cables through which
the open-wire lines extend into the central office, either directly on protectors or on ter-
minal blocks, from which the lines are connected to protectors. The protectors, consisting
of heat coils (or fuses) and carbon block discharge gaps, function to prevent excessive for-
eign currents or voltages from damaging the central-office cables and equipment, as dis-
cussed in more detail in Sections 10 and 17. Office circuit fuses are also provided to pre-
vent excessive office currents from damaging the equipment or wiring.
Testboards or line-terminal switchboards, to which the lines are extended from the
protector frames in cable, are designed to terminate the telegraph circuits, entering an
office, in jacks for testing, patching, and other purposes, as required in maintaining and
operating these circuits. Certain central-office equipment units, battery taps, and special-
purpose apparatus are also terminated at such boards and may be associated with or dis-
connected from the various circuits, to meet operating needs. In the older-type boards
telegraph-circuit layouts are usually established in part by means of patching cords; in
the latest-type boards, these circuits are wired through groups of jacks, individual to each
circuit, eliminating the need for patching cords, except for testing or establishing other
than the normal circuit layout.
Intermediate distributing frames have mounted, on their two sides, terminal blocks,
to which the various equipment units in the office are wired. Office cables also extend
from these frames to testboards and line-terminal switchboards and to telegraph operat-
ing positions and teletypewriter switchboards, so that by means of crossconnections on
these frames circuits may be connected to the various test board and switchboard jacks,
operating positions, and equipment units, as desired.
Teletypewriter switchboards employed for the purpose of establishing connections be-
tween teletypewriter subscribers consist principally of positions equipped with jacks, cord
circuits, and a keyboard sending and receiving teletypewriter, which may be associated
by means of keys with any cord circuit on the position.
The operator handles connections somewhat like an operator at a manual telephone
switchboard position, the principal difference being that the incoming calls are answered
and extended to the called subscriber by operating the teletypewriter, with the assistance
of similarly equipped distant operators, if necessary.
These boards are designed to serve as few as 10 lines (mostly for private networks) or as
many as 2040 subscriber lines and 600 intertoll trunks, when the outward, inward, and
through traffic is handled at one board.
In order to improve transmission from a central office to a teletypewriter station, a
wave-shaping network, consisting of resistance, inductance, and capacitance of various
values and combinations, depending on the type of loop and connected equipment, is fre-
quently inserted in the side of the loop connected to the repeater at the central office.
Wave-shaping networks are also employed, as required, at the stations. These networks
assist in restoring the received signal wave to its original shape.
The jacks, cords, and plugs used at telegraph switchboards and testboards for testing,
patching, and establishing connections may be of standard types, such as those in manual
telephone testboards and switchboards. However, where low-resistance conductors with
greater service margins are needed, these units are frequently of heavier construction.
The number of conductors will vary between different boards, depending on the circuit
requirements.
Telegraph repeaters employing polar transmission are standard for d-c trunk-line
terminal sets; they usually operate on a full duplex basis with ground return. Other types
of repeaters are used at intermediate trunk-line points for transmission reasons. The
operating functions of repeaters have been discussed in article 6.
Repeaters are used in various arrangements in circuits, the name by which they are
designated indicating the manner in which they function, such as a combination duplex-
duplex half repeater, terminal duplex-duplex half repeater, and high-speed polar duplex,
high-speed single-line, and regenerative repeater. One form of repeater provides for
receiving, recording, and, when the outgoing circuit is clear, retransmitting telegraph sig-
nals, which, in effect, is equivalent to storing signals. Special types of repeaters serve
other purposes, such as connecting multiplex channels to other channels and loops.
18-48
TELEGRAPHY
Relays perform vital functions in the operation of telegraph circuits and equipment.
The modern high-speed polar relay operates efficiently and with precision. Figure 1
shows a common type of polar relay for
use in high-speed d-c telegraph circuits.
Figure 2 shows a plug-type polar relay,
commonly used in d-c telegraph line cir-
cuits. Many other types of relays are em-
ployed in telegraph circuits, each designed
to perform its particular function.
Multiplex distributors, as previously ex-
plained in this section, are devices having
segmented and solid ring face plates, with
which rotating brushes are in contact, and
by means of which telegraph signals from
one or more circuits are transmitted over
a single telegraph line in sequence on a
time-sharing basis. The face plates are
removable and may be changed as desired
to meet operating requirements.
The brushes are mounted on a shaft,
driven by an impulse motor, which is syn-
chronized with the motor of a multiplex
set at the distant line terminal. For this
reason, the start and stop pulses are not
required, as they are for the teleprinter or
teletypewriter, and only a five-unit code is
employed per character for each circuit
operating over the multiplex line.
The shaft between the motor and the
brush assembly consists of two parts joined
together by a magnetically operated ratchet
device, by means of which the angular posi-
FIQ. 1. Typical High-speed D-c Telegraph Polar
Relay (Courtesy Western Union Telegraph Co.,
A.I.E.E., F. E. D'Humy, and P. J. Howe)
tion of the brushes with respect to the motor rotor may be changed in steps of 1 1/2 angular
degrees. The change may be made with the motor operating, if desired. A mercury-
filled flywheel mounted on the motor shaft
provides stability of rotation. The various
connections to the distributor are brought
out to multicontact bayonet-type plugs
to provide for rapid replacement of the
distributor in case of trouble. Figure 3
shows one type of multiplex distributor.
The shaft speed is determined by the
required channel speed. For four-channel
operation in each direction, at a channel
speed of 66 words per minute, the shaft
speed is about 396 rpm. However, the
total message capacity for the line is 528
words per minute.
Synchronization of speed between two
multiplex sets at opposite ends of a mul-
tiplex circuit is accomplished by means
of a driving fork associated with each set.
This fork is magnetically vibrated and
equipped with contacts to generate im-
pulses from a d-c supply for operating the
motor of the set. The frequency of vibra-
tion of the fork, and hence the motor
FIG. 2. Typical D-c Telegraph Relay for Line and
Other Circuits (Courtesy Western Union Telegraph
Co., A.I.E.E., F. E. D'Humy, and P. J. Howe)
speed, may be altered by changing the
position of weights clamped to the fork
tines. The normal fork frequency (with-
out weights) is about 60 cycles per second,
corresponding to a distributor speed of about 360 rpm. Forks with shorter tines are used
for high-speed circuits. Figure 4 shows a drawing representative of a driving fork.
The tape perforator consists of a perforating mechanism, actuated by a keyboard unit,
in which each individual key lever, with certain exceptions, is designated with an upper-
CENTRAL-OFFICE EQUIPMENT
18-49
and lower-case character. By operating the key levers when the perforator is in its operat-
ing condition, the characters corresponding to the keys operated will be punched in a
paper tape in the standard five-unit code. *--~~
FIG. 3. Typical Rotary Distributor (Courtesy Western Union Telegraph Co., A.I.E.E., F. E. D'Humy,
and P. J. Howe)
In one type of perforator design, a punch block contains six small cylindrical metallic
fingers or punches, between the die plates of which block the tape is fed (see Fig. 5) . A
punch hammer, operated by a magnet, forces the punches through the tape as it passes
the punch holes in the die plates. As each character is punched, the tape is moved for-
ward one space by a pawl and feed roll, and the succeeding character is then punched.
Five of the punches are for code perforations, and the sixth punch provides the feed holes
in the center of the tape.
Between the punch hammer and the five punches are five punch bars, which are con-
nected by bell cranks to five U-shaped bars (loops), pivoted at each end and held by
FIG. 4. Driving Fork Used in Multiplex Systems
means of springs so that their greatest length is in a horizontal position directly beneath
the keyboard.
Attached to the lower edge of each key lever is a piece of metal, called a comb, which is
cut out, so that depressing a key will cause its comb to strike the top edge of one or more
of the loops and move them downward. The combs are cut differently for the different
keys, resulting in a different combination for each key depressed.
18-50
TELEGRAPHY
The depression, of any loop moves the corresponding punch bar from in front of its
punch so that, when the punch hammer is operated by the magnet, the corresponding
punch does not operate and the tape is not perforated by that punch. A sixth (power)
FIG. 5. Perforator Punching Mechanism (Courtesy Bell System)
loop, operated when any key is depressed, energizes the punch magnet, which actuates
the punch hammer.
This perforator also provides for moving the tape backward for correction of errors and
for indicating end of a line, so that the carriage return key can be operated to start a new
line at the distant receiving machine.
The typing reperforator is a device for receiving messages from a telegraph circuit or
transmitter and recording them in tape by five-unit code perforations and by printing the
character on the tape above the corresponding perforations.
The transmitter and transmitter-distributor are devices for translating code perforations
in tape into electrical impulses, which are transmitted over a connecting medium to a re-
ceiving device for interpretation as signals of intelligence. The perforations may be in a
five-unit, six-unit, or other code, depending on the particular circuit requirements.
pper (spacing) contacts
Start segmen
_ Contact tongues
III S-topsegm e nt-
Line battery
(marking) contacts
Distributor brus!
Commutator
FIG. 6. Diagram Showing Transmitter Contacts Wired to Distributor Segments (Courtesy Bell System)
In the transmitter-distributor the tape transmitter establishes the code combinations to
be transmitted, and the commutator distributor sends out these combinations over the
line, as marking and spacing impulses, in their proper sequence and at the desired speed.
Both units are driven by the same speed-regulated motor.
For one type of five-unit code transmitter-distributor, the five contact tongues (see dia-
gram hi Fig. 6) of the transmitter move between two sets of contacts, one set marking and
STATION EQUIPMENT
18-51
the other set spacing. These tongues and the multipled marking and spacing contacts are
connected to distributor segments. In "make-break" operation, battery is connected to
the marking contacts only.
The tongues are mechanically connected to the ends of five pivoted contact levers, each
of which has three extensions A, B, and C, as shown in Fig. 7. In the unoperated position
of the contact lever bail (the position shown in Fig. 7) , the contact lever springs pull down
on the A extensions, causing the tape pins in the C extensions to press up against the
tape but the upper contacts remain closed. Since the tape pins are spaced the same
distance apart as the tape perforations, any pin will then pass through the tape if there is
a perforation in the tape above it. When a pin moves through a perforation, the A exten-
sion is permitted to move down slightly under action of its spring, thus opening its spac-
ing and closing its marking contact by the movement of its contact tongue. Where there
is no perforation in the tape above a pin, the pin is held in its normal position against the
Upper (spacing^
contact screw" ~^
Terminal
Note: Tape pta shown
extending upward through
perforation In tape.
-Operating lever
FIG. 7. Tape Transmitter Mechanism (Courtesy Bell System)
tape and its contact tongue remains on spacing. Thus, the code perforations in the tape
determine the setting of each of the contact tongues either to marking or spacing, and
hence the polarity of the distributor segments connected to the tongues.
After each character is transmitted, the contact tongues are reset to spacing by opera-
tion of the operating lever and contact lever bail. This bail moves the B extensions to
the left, withdrawing the tape pins to a position below the tape guide surface, thus mov-
ing the contact tongues upward. Also, after each character is transmitted, a sixth (feed)
lever is actuated, causing the tape feed mechanism to move the tape forward a distance
equal to that between the character punches in the tape.
An automatic stop is mounted on the transmitter-distributor base to stop the trans-
mitter if the associated perforator operation is interrupted or if its speed becomes less
than that of the transmitter. This avoids tape mutilation by the transmitter. The stop
consists of a light metal lever, suspended over the tape loop between perforator and trans-
mitter, which is raised when the loop becomes tight, opening the control circuit of the
transmitter.
Message conveyors are employed in the larger telegraph central offices to reduce the
travel and handling time for messages that must be transported from one location to
another in the same office or building. In the largest centers, the total number of mes-
sages handled daily may average 300,000 or more.
Pneumatic tubes provide a rapid and efficient means of transporting the original copies
of messages, being commonly employed between branch and central offices and for intra-
departmental use in large central-office buildings.
14. STATION EQUIPMENT
Station equipment intended for telegraph purposes is of various types and designs to
meet the needs of the customer. A number of the equipment units are also applicable for
use at customer premises, such as the teletypewriter, teleprinter, perforator, typing re-
18-52 TELEGRAPHY
perforator, transmitter-distributor, Telefax, ticker, clocks, and various other units. The
station equipments discussed in the following paragraphs are additional to those previ-
ously discussed.
Printers. Two types of teletypewriters of the start-stop, five-unit code type have not
been previously described. One is a motor-driven, single-magnet, fixed paper carriage,
typebar, page printing type, operating normally at speeds of 240 to 368 operations (40 to
60 words) per minute. The paper may be in single sheet rolls, usually 8 or 8 1/2 in. wide,
or two or more carbon copies may be made by using the proper paper assemblies.
The other is a teletypewriter, used where not more than one carbon copy is required
and where a smaller machine than the first is desired by the customer. This machine is
a motor-driven, single-magnet, moving paper carriage, typewheel, page printing type,
operating normally at 368 operations per minute. It uses paper 8 1/2 in. wide, which may
be multiple wound for one carbon copy.
Radio-interference-suppression apparatus (filters), consisting of inductance, capaci-
tance, and resistance, are employed in station equipment, usually in a parallel-series rela-
tion, across various make-break contacts in the teletypewriter or teleprinter. One type
of suppressor reduces induction at broadcasting frequencies, and another type provides
suppression at both broadcasting and higher frequencies.
Selectors are used on important circuits to provide a convenient means for calling
attendants at repeater or terminal stations to the circuit when trouble develops. They
are also used on Morse wires and concentrators to enable one station to call another with-
out calling in all the other stations on the same circuit. The selector, Fig. 8, contains a
FIG. 8. Typical Telegraph Selector
magnet, normally connected with the line or line relay, which controls a mechanism
arranged to close a set of local contacts only when the magnet is operated by the particular
combination of impulses for which the selector mechanism is adjusted. The local contacts
of the selector may be used to operate either visual or audible signals or to place the local
receiving apparatus in an operative condition. Signal combinations for operating the
selectors may be transmitted manually with a Morse key, or special clockwork-driven
calling keys may be used for the purpose.
In Morse telegraphy manual operation is employed, but, owing to the growth of auto-
matic transmission of messages, Morse operation is confined mainly to occasional local
services over short-haul telegraph facilities, such as those to sporting-event locations,
railroad-station offices, and small towns.
Morse circuits are operated either single or duplex, as conditions may require. Where
several such circuits terminate at a central point, they are usually connected into a con-
centrating unit by means of which one operator can handle all the circuits so concen-
trated. •
Figure 9 shows sketches of a Morse sending key, sounder, and relay.
The sending key has two contacts, normally held open by a spring, which are closed
by manually depressing a key lever, which also depresses the spring. When the key is
released, the spring causes the contacts to open. A second lever operates horizontally to
close the circuit at the key when the key is not in use.
The sounder consists of an electromagnet and an armature which moves a sounding
lever between two adjusting stop screws, the assembly being mounted on a sound-amplify-
TRANSMISSION STANDARDS
18-53
Morse Sending Key
ing base. When the magnet is energized, the armature is drawn down until its stop screw
contacts the metal frame, producing an audible click. When the magnet is de-energized,
the armature is restored to its unoperated posi-
tion by spring action, its outer end striking the
upper stop screw, which produces a click.
Two of these clicks separated by a short inter-
val are interpreted by the operator as a dot. For
a longer interval between clicks (usually three times
the interval between dots), the signal is interpreted
as a dash. The armature travel and restoring
spring tension can be adjusted to suit the operator.
Local sounders operate in local sounder circuits;
they may be of low resistance (about 4 ohms),
requiring an operating current of about 250 ma,
or of high resistance (100 or 400 ohms), requir-
ing operating currents of f about 60 and 30 ma,
respectively. Main line sounders are designed
for operation in series with the main line cir-
cuit. These sounders may be adjusted so that
their operation is not materially affected by line
leakage, usually encountered, and their resistance
may be 30, 100, or 120 ohms, depending on circuit
requirements.
The relay consists of an electromagnet having one
or more windings arranged to move an armature,
which operates between a set of contacts. Signal-
ing impulses, passing through the operating wind-
ing of the relay, cause the armature to move to
its proper contact, in accordance with the type
of impulse received, thus repeating the sent signals
in a local circuit connected to the relay contacts.
The type of relay shown in Fig. 9 usually is
equipped with a magnet having 25, 100, or 150
Morse Relay
FIG. 9. Telegraph Apparatus Used at
ohms resistance. Manual Stations
TRANSMISSION-MAINTENANCE
By John D. Taylor
15. TRANSMISSION STANDARDS
Signal transmission is considered perfect in any telegraph circuit or connection if the
received effective marks and spaces or dots and dashes are exactly the same length as the
sent marks and spaces or dots and dashes. In practice, signals which may be nearly per-
fect as sent are affected during transmission by circuit constants, such as the inductance,
capacitance, resistance, and leakage of the line conductors, by equipment characteristics,
and by various forms of interference. It has been found that, with present operating
arrangements, bias changes, large fortuitous distortion (usually termed "hits")* and
smaller but more frequent fortuitous distortion (see discussion in Article 5) are the princi-
pal causes of transmission impairment.
In designing telegraph facilities, both line and equipment, the general problem is to
provide a satisfactory grade of service in the most economical and convenient manner that
will meet public and operating needs. The trend is toward automatic transmission in the
telegraph just as it is in the telephone field, in order to increase the speed of service most
efficiently.
Because of the many types of facilities employed in the telegraph plant, different tele-
graph circuits affect telegraph signals differently, and, in order for the signal transmission
to be satisfactory in any given circuit layout, it is necessary to know in advance what
these effects will be.
Since, in the present state of the art, distance is not a limiting factor in the transmission
of telegraph signals, direct telegraph circuits may be provided from any point to any other
point in the world by choosing the proper equipment and transmitting media for such
circuits.
18-54
TELEGRAPHY
16. TRANSMISSION COEFFICIENTS
One of the large communication companies in the United States in 1926 developed a
system (since improved) of transmission ratings of telegraph circuits and equipment,
based on signal-distortion measurements and on experience gained from operating per-
formance. This system is based on the fact that, since the distribution of distortions
follows the normal distribution law, ratings or coefficients, chosen as proportional to the
mean-squared values of the distortions, could be added directly to give the overall co-
efficient for any combination of circuit units for which coefficients were available.
•4.9-
orofc
Doard
rcuit
Voice
frequency
In cable short
subscriber*
line
, Subscriber"
station in
Baltimore, Md
©asper, Wyo,
Denver, CoL Chicago, III, New York, N~.Y. Baltimore^ M<L
Numerals are transmission, coefficients
FIG. 1. Diagram of Typical Teletypewriter Exchange Service Connection Requiring a Regenerative
Repeater (Courtesy Bell System)
The magnitude of these coefficients was selected so that, for satisfactory signal trans-
mission, the overall combined coefficient should not exceed a value of 10. Where this
value was exceeded in a given circuit layout, it would be' necessary, by some means, to
reduce the signal distortion. For start-stop telegraph equipment, the regenerative re-
peater is available for correcting signal distortion. It is customary to insert them in a
circuit or at the junction of circuits to limit the overall coefficient to 10, as shown in Fig. 1.
Duplex telegraph repeaters of the differential type are employed at intermediate points
in long d-c telegraph circuits with ground return to increase signal strength. These re-
peaters are usually spaced about 250 miles apart, although this distance varies over a
comparatively wide range, depending on the types of line facilities, equipment, interfer-
ence, operating speeds, and other factors involved. These intermediate repeaters do not
correct distortion but repeat the signals through from section to section. For this reason,
regenerative repeaters or other distortion-correcting devices are generally required every
two or three repeater sections.
17. CROSSFIRE
Crossfire neutralization between polar duplex grounded telegraph circuits is necessary
where this form of electrical interference becomes objectionable. As the speed of opera-
tion increases, crossfire between such circuits assumes greater importance.
Sending end
WIrel
Filter
Receiving encf
- >Une current
—— •*• Crossfire current
*•«•*' Neutrallztpg current
FIG. 2. Neutralization of Crossfire Current at the Sending Terminal (Courtesy Bell System)
MAINTENANCE
18-55
Crossfire is caused by the mutual inductance and capacitance between the telegraph
circuits and by leakage. Though the major part of this interference is due to the close
physical relation between the paralleling open wires and cable conductors, some of it re-
sults from couplings in equipment common to two or more of the paralleling conductors,
as in composite sets, line filters, and loading coils. In general, the magnitude of the inter-
ference is proportional to the length of the line wire and cable conductor parallel. In cable,
the coupling is much greater than in open wire, and, if more than two duplex telegraph
circuits are derived from one quad, the crossfire usually becomes prohibitive, even for
comparatively short distances, unless neutralization is applied.
Figure 2 shows one method of neutralizing crossfire currents at the sending end without
affecting these currents at the receiving end of a polar duplex circuit. Figure 3 shows one
Sencflng
Filter
Receiving end
— >-Llne current
— ^-Crossfire current
^^Neutralizing current
Fia. 3. Neutralization of Crossfire Current at the Receiving Terminal (Courtesy Bell System)
method of neutralizing crossfire currents at the receiving end without affecting these cur-
rents at the sending end of a polar duplex circuit. In some cases, neutralization at the
sending or the receiving end only will be sufficient; in the more severe cases, both methods
will be required.
For sending end neutralization, a properly adjusted condenser is employed between the
artificial lines of the two circuits shown, causing currents to be set up between them in an
opposing direction to the crossfire currents. For receiving end neutralization, a trans-
former is inserted in the apexes of the two duplex sets, which, by proper poling and adjust-
ment of the coupling, sets up currents opposing the crossfire currents.
18. MAINTENANCE
The proper maintenance of telegraph facilities plays a vital part in providing the public
with telegraph service of a satisfactory grade. For this purpose, various types of test-
boards and testing equipment have been developed and routines established to insure
that the facilities are properly maintained.
TESTING EQUIPMENT developed for maintaining telegraph facilities includes such
principal units as:
1. Monitoring machines with sending and receiving units, for checking the transmission
of telegraph signals.
2. Test distributors, sending substantially perfect signals for lining up and testing tele-
graph circuits and apparatus. One type is for the central-office and another for portable use.
3. Automatic multiple senders, providing sources of battery reversals and of test signals
for teletypewriter circuits.
4. Telegraph signal biasing sets, providing sources of biased battery reversals and tele-
typewriter test signals of the inverse neutral type; also providing for measuring bias from
a distant sending end.
5. Telegraph transmission stability test set, giving quantitative indications on a recording
meter of the freedom from bias of a series of received reversals.
6. Telegraph station test set, for testing at outlying stations or small central offices, to
indicate distortion of received signals and assist in determining wave-shaping network
requirements.
7. Telegraph transmission measuring set, indicating directly on meters the distortion in
signal reversals from start-stop machines. One meter indicates bias (average) distortion
and another meter the peak value of the total distortion (instantaneous sum of bias, char-
acteristic, and fortuitous effects) . One type of set is for the central office and another is
for portable use.
8. Telegraph crossfire test set, for determining the proper values of capacitance and re-
sistance for neutralizing sending-end crossfire and the proper inductance couplings for
neutralizing receiving-end crossfire between grounded polar duplex telegraph circuits.
18-56 TELEGRAPHY
9. Hit indicators, giving locked in indications of short-duration line disturbances, suffi-
ciently large to cause or almost cause the receiving relay to leave its marking contact, or
when an initial spacing impulse of a message is received from the line.
10. Qrienttftion-testing'indicator {portable type), for adjusting the orientation of a certain
type of regenerative repeater,
11. Hit suppressor unii^ for preventing certain forms of interference on private-line
telegraph facilities from being transmitted in a certain direction beyond the line section
or sections in which the hits occur.
12. Carrier telegraph test set, for maintaining carrier telegraph systems, including fila-
ment circuit tests and a drift measuring circuit for compensator relay bias adjustments.
13. Frequency-measuring devices, for checking carrier frequencies used in carrier tele-
graph systems.
BIBLIOGRAPHY
General References
1. Bell Telephone System Practices.
2. A.I.E.E. Transactions.
Special References
1. F. E. D'Humy and P. J. Howe, American Telegraphy After 100 Years, AJ.E.E. Trans., Vol. 63,
1944.
2. O. E. Pierson, The Western Union Varioplex Telegraph System, Electrical Communication, Vol.
22, No. 2.
3 C. H. Cramer, Some Modern Techniques in Ocean Cable Telegraphy, AJ.E.E. Technical Paper
47-79, December 1946.
RADIO TELEGRAPH SYSTEMS
By J. L. Finch
In radio telegraph communications it is necessary to have a transmitter, and a receiver
and an operator's position. For the less important circuits these are often located together
under the control of one operator who alternately sends and receives messages. This
method of operation is known as the simplex method. For more important circuits the
transmitter and the receiver are arranged for simultaneous operation, and this is known
as the duplex method. In the duplex method it is usually advisable to have the trans-
mitter and receiver located at different points to reduce interference troubles. This
arrangement becomes increasingly important as more transmitters and receivers are used.
When it is necessary to locate the transmitters and receivers at the same point, as on ship-
board, special precautions must be taken to prevent mutual interference and the frequency
separation between transmitted and received signals must be kept relatively great.
When ratio communication is carried on. to and from large cities it is the usual practice
to have a central office in the city with both the transmitting and the receiving centers
located well outside the city and connected by wire lines or by ultra-high-frequency radio
control circuits.
19. CHOICE OF TRANSMITTER AND RECEIVER SITES
The sites are usually chosen where ample level space is available for directional antennas
for each communication circuit planned. The availability of a dependable power supply
and of reliable control channels is a further consideration. The receiving centers are
usually located where man-made static is low. It is desirable that hills and mountains in
front of the antennas do not rise at an angle of more than 3° for long-distance communica-
tion at short waves, although angles of as much as 5° can usually be tolerated. For
shorter distances the angles may be greater. The land immediately in front of an antenna
has a direct bearing on the vertical directivity and should be level. For long waves, moun-
tains and valleys within a fraction of a wavelength have little effect on the antenna direc-
tivity.
20. CHOICE OF FREQUENCIES
The most desirable frequency to be used between any two points depends upon many
factors which vary with time of day, season of year, position in the sunspot cycle, occur-
rence of magnetic storms, and location of the great-circle path over which the signals must
REDUCTION OF FADING EFFECTS 18-57
travel with respect to the aurora areas centered about the earth's magnetic poles. These
factors are mostly related to wave propagation and are described in article 10-23. Usable
frequencies start at about 10 kc and extend as high as 30,000 Me. The very low frequen-
cies are propagated effectively and are relatively steady and consistent, but they require
very large and expensive antenna systems, particularly at the transmitting end, in order
to radiate even a small percentage of the generated power. At the receiving end extensive
antennas are required to get good directivity and thus a favorable signal-to-noise ratio.
Further, the transmitting antennas must be very sharply tuned in order to be efficient, and
this fact limits their modulation capabilities to relatively low keying rates. It should be
noted that propagation at frequencies from 50 kc to 30 Me is subject to wide fluctuation.
Commercial companies have found it worth while to maintain and operate long-wave
facilities which are already in existence for use during magnetic storms and to serve for
re-establishing contact with the remote points after short waves have suddenly faded out.
Frequencies between 3 and 25 Me have been found the most useful for long-distance
communications. Those between 3 and 10-13 Me are useful over these long distances
when most or all of the radio path is in darkness while those from 10-13 to 25 Me are
useful when most or all of the path is in daylight. The lower of these frequencies are
useful over shorter distances in the daytime. The same frequencies can be used succes-
sively in different parts of the world as the daylight and darkness areas progress around
the earth.
Frequencies above 30 Me are rarely useful for extensive periods for long distances (over
2500 miles) and those above 50 Me can be relied upon as a rule not to carry to distant
points on the earth's surface and so can be used over and over again on circuits separated
by only a few hundred miles. Because signals at these higher frequencies will not bend
very much, an optical path or one approaching an optical path between the transmitting
and receiving antennas is necessary.
21. REDUCTION OF FADING EFFECTS
The use of short waves for communicating over long distances is very frequently beset
with fading caused by the alternate addition and subtraction of the signal arriving over
different ether paths. This is due to the varying phase relation of the arriving radio-
frequency waves. It has been found that much of this fading is very local in character.
When a signal has faded out at one location it may be coming in at full strength a few
hundred feet away. Also when at a given point one radio frequency has faded out com-
pletely, another frequency only a few hundred cycles different being radiated from the
same transmitting antenna may be corning in at full strength at this point. Receiving
systems which employ two or more receiving antennas spaced apart geographically are
known as space diversity receiving systems. The telegraphic signals received by each antenna
are rectified and passed through a limiter which cuts off the tops of all the characters that
would exceed a certain value. The various signals are then combined in such a manner
that all of them must fade at once to cause a signal failure. When using three separated
receiving antennas this diversity effect reduces the failures due to fading to a very small
fraction of that suffered by the signal received on any one of the antennas. Systems that
transmit two or more slightly different radio frequencies from one antenna are termed
frequency diversity systems. In this case the same receiving equipment is used as otherwise,
since the different radio frequencies being received are so close together that the receiver
responds to all of them substantially equally. The limiting used is such that all frequencies
must fade out at once to cause a signal failure. This system results in a very marked in-
crease in the reliability of the circuit.
To obtain the different frequency components required in the transmitter output for
frequency diversity it is usual to phase-modulate the carrier at an audio rate of about
600 cycles and with a maximum phase deviation of about 1 radian. This modulation
results in the production of two side frequencies spaced 600 cycles each side of the carrier.
The amplitude of each side frequency is a little less than half the amplitude of the unmodu-
lated carrier. Phase modulation can be accomplished quite simply, and it does not neces-
sitate reduction of the total power generated by the transmitter.
It is common practice to key two different transmitters operating at different frequen-
cies with the same signals and to combine the outputs of two receivers at the traffic office
to insure against service interruptions, particularly at the time of day when one of the
frequencies is about to fade out and it is desired to replace it with another.
18-58 TELEGRAPHY
22. RADIO INTERFERENCE
Interference between radio channels should be eliminated by spacing the frequencies
sufficiently far apart and by making the receivers selective enough to differentiate between
the desired and undesired signals. The radiation at unauthorized frequencies such as at
harmonics of the desired frequency wave must be avoided. In some types of transmit-
ters, frequencies lower than the desired ones are generated and then the desired harmonic
is radiated. The radiation of these lower frequencies must be avoided. Vacuum-tube
transmitters are prone to generate spurious or parasitic frequencies. The radiation of
such frequencies must be avoided. These parasitic frequencies often modulate the desired
frequency wave, resulting in modulation sidebands which will be radiated with the desired
wave if allowed to exist and will cause interference on other channels. Often when a
transmitter is free from parasitic oscillations in the steady state, both marking and spac-
ing, such oscillations occur during the transient period at the beginning and end of signal-
ing characters. These oscillations are known as key-click parasitic oscillations. Other
interchannel interference sometimes results from the modulation products or side fre-
quencies generated by the keying, these being particularly noticeable at high signaling
speeds and when the characters are square ended. To round the characters to reduce these
side frequencies when using efficient class C amplifiers in the transmitter and with on-off
keying is difficult and expensive. When using "frequency shift" or "two-tone" keying,
however, the signal characters can be rounded quite simply and the objectionable side-
frequency radiations greatly reduced. Two transmitters at the same station, particularly
when operating at closely spaced frequencies, sometimes intermodulate each other and
radiate signals in adjacent bands. This can usually be made negligible by reducing the
cross coupling between the two systems.
Receivers may cause interference with other receivers, usually due to radiation from the
first heterodyne oscillator into the room and into the receiver power wires and into the
receiving antenna. It is particularly important to avoid radiation back into the antenna
of a level of more than 1 microvolt when one antenna is used with a number of receivers
at various and variable frequencies.
23. FREQUENCY SHIFT BUYING
It has been the general practice in the past to key transmitters by interrupting the
transmitter output power. Recently equipment has been developed to take advantage of
the "frequency shift keying" system, also known as the "two-tone keying" system. This
method employs one radio frequency for "mark" and a second radio frequency for "space,"
each at the same power. The separation between the two is not critical. At present a
separation of 850 cycles is in common use. To reduce key-click interference in adjacent
channels it is desirable to shift the frequency of a single oscillator and at a rate only suffi-
cient to accommodate the required keying speed.
In receiving frequency shift signals, amplitude variations are limited out by the use of
a limiter stage. The resulting signals of fixed amplitude and variable frequency are im-
pressed upon a discriminator the output of which may operate a relay device, tone keyer,
or other utilization device. The limiter stage largely eliminates the effect of atmospheric
or other interference whose strength is lower than 3 db below the signal.
Results have indicated that in practice the transmitter power can be reduced as much
as 10 db, after adopting the frequency shift keying system, without degrading the service.
24. TRAFFIC OFFICE AND EQUIPMENT
In central offices carrying small volumes of traffic, particularly over radio circuits of
inferior reliability, it is advantageous to have the transmitting and receiving positions
located adjacent to each other. This is for convenience in asking and giving acknowledg-
ments and for "breaking" the circuit. For handling larger volumes of traffic over a num-
ber of reliable circuits, it is advantageous to arrange the transmitting positions in one
group and the receiving positions in another.
Intelligence can be transmitted over radio telegraph circuits in the Morse code or by
means of automatic printers using their own special codes. For the simplest equipment
Morse signals are transmitted by hand and received aurally and transcribed by hand or
on a typewriter. For higher speeds and more reliable service automatic sending and re-
ceiving is used. The messages are punched on a typewriter-like machine known as a
TEAFFIC OFFICE AND EQUIPMENT 18-59
perforator. A sample tape is shown in Fig. 1. The tape is run through an auto-head device
which has electrical contacts and which form the Morse characters corresponding to the
letters punched. The received signals operate an ink tape recorder. These recorders com-
monly involve a moving tape with a pen pressed against it. The pen is retained in its
lower position for "space" and in its upper position for "mark," making a record as shown
in Fig. 1. Automatic Morse communication is practical at speeds of 20 to 500 words per
minute.
For average speeds up to 40 or 50 words per minute one operator at the transmitting
end perforates the tape and tends to the auto-head machine. At the receiving end one
operator views this tape as the message is recorded and transcribes the messages on a
typewriter. For higher speeds of transmission the tape must be punched by two or more
operators and sections fed successively into the auto-head. The recorder tape must be
divided between two or more receiving operators for transcription.
Automatic printers are advantageous in that they make it unnecessary for the operators
to learn the code, they reduce human errors in transcribing from code signals, and they
permit automatic transcription of incoming messages directly in a form suitable for de-
livery to the customer. Their use, however, eliminates the possibility of detecting errors
Auforrraflc Transmitter Tape __^__
nn noon nnnn nnn n nnnn nnn
Recorder Tape
FIG. 1. Tapes for Automatic Sending and Receiving
due to mutilation of the signals introduced in the radio path. Frequently a trained opera-
tor can transcribe correctly a mutilated signal such as would cause a printer to make an
error or to operate an error-indicating device. Further, the transmission speed is limited
to that at which a printer will function properly, i.e., to speeds of 60 to 100 words per
minute. The printers in general use employ a five-unit code and respond to any combina-
tion of signals whether mutilated or not. An error-indicating printer is in use which
employs a seven-unit code. All operations use three marking and four spacing elements.
Any other combination will operate an error-indicating device.
In connection with radio telegraphy it is customary to rate transmission speeds in words
per minute, each word consisting of an average of five letters. More accurately, each word
consists of 48 units * or minimum elements, each unit being taken as the length of one
dot or one space between dots, and the length of dashes and spaces between letters being
equal to three units. From this it can be calculated that when the auto-head is running
at a rate to make 40 dots per second the transmission rate will be 100 words per minute.
Similarly printer speeds are calculated on the basis of six operations per word, allowing
five characters and one space per word.
MULTIPLEX. In order to make use of the high signaling speed capabilities of short-
wave radio circuits and still enjoy the advantage of automatic printer operation at nominal
speeds, means have been devised for dividing the total time available for transmission be-
tween two or more channels. This system is known as time division multiplex (see article 7) .
This system can also be used for Morse operation; it is advantageous because each channel
can be copied as it comes in, and thus delays in message delivery caused by the necessity
of dividing tape received at high speeds between two or more operators can be avoided.
MULTICHANNEL. A second method of obtaining more than one telegraph channel
on a single radio circuit utilizes single-sideband equipment such as has been developed
primarily for telephone service. Such a system can carry a large number of individual
tones, each keyed as desired with printer signals or Morse signals and each separated from
the others at the receiving end by means of wave filters.
Both the multiplex and the multichannel systems are more expensive initially and more
costly to maintain and operate than single-channel systems, but they are worth while
when large volumes of traffic are to be handled because they save space in the radio spec-
trum and at the same time provide for printer operation or Morse operation at speeds that
can be transcribed currently.
* The term "baud" has, in some sections of the industry, been applied to these units. In the offi-
cially correct usage the baud is the unit of telegraphic speed or of rapidity of modulation corresponding
to one minimum element per second.
18-60
TELEGKAPHY
25. CONTROL CHANNELS
The signals must be carried from the central office to the transmitting station, and from
the receiving station to the central office, over suitable control channels. These channels
can be carried over wire lines or over ultra-high-frequency radio circuits. When wire lines
are available d-c signals may be used, either unidirectional or polarized (plus and minus),
or keyed tone signals may be employed. The tone signals have the advantage that a
number of them can be carried over one tone pair and separated by wave niters (see art-
icle 11-10). When ultra-high-frequency radio control circuits are used, keyed tone signals
are employed. A number of similar groups of tone signals can be transmitted over a single
radio circuit by a system similar to the voice-carrier system as described in article 17-9.
TONE KEYERS. The keying device or tape transmitter device in the central office
usually closes an electric circuit by means of a pair of contacts for marking and opens it
for spacing. This action is made to key a tone by means of a tone keyer such as that
shown in Fig. 2. The equivalent results can be accomplished by purely electronic means
kD-c transient
' balancex
Key
-i20V ^ +380 V
PIG. 2. Circuit Diagram of a Tone Keyer
applying the same general principles. Tone keyers are also used at the receiving station
by means of which the incoming signal is made to key a tone for transmission to the central
office.
TONE SIGNAL CONVERTERS. At the transmitting station the tone signals must
be converted into d-c signals to key the transmitter. The device for accomplishing this is
known as a tone signal converter and may take the form shown in Fig. 3. This embodies a
-4 .V -i--,
J _ _-400V \
Tone slgnaj convorter Threshold
FIG. 3. Circuit Diagram of a Tone Signal Converter
threshold device for suppressing low-level noise and for preventing tails on the characters
from causing "heavy" signals. It embodies a Umiter for cutting off the tops of the signals
and a low-pass filter to smooth out the rectified tone and thus to keep the signals from
being modulated by the tone itself. The gain control is used for setting the level of the
CONTKOL CHANNELS
18-61
tone signals, which usually have been rounded by passing through the wave niters of the
tone channel to give the correct "weight" of signals in the transmitter. Lowering the
gain makes the signals lighter, and raising it makes them heavier.
RECORDER DRIVE. At the central office the incoming tone signals must be con-
verted to direct current to drive the ink tape recorder or printer relay. The device for
accomplishing this may take the form shown in Fig. 4. A simple tone rectifier circuit will
usually suffice for driving the printer relay for printer service.
Rfectlfier
Recorder
. ^ ^ :fc350V
'"Space" currenis '"Made"' currents
FIG. 4. Circuit Diagram of a Recorder Driving Unit
BANDWIDTHS. The transmission of keyed tone signals requires a definite band
which must have a width roughly proportioned to the keying speed. Satisfactory service
may be achieved by allowing for the transmission of no more than the first side frequency
of the keying speed under stable input conditions and stable transmission characteristics
such as are normally achieved in first-class lines. Thus for 125 words per minute Morse,
i.e., a keying frequency of 50 dots per second, the usable channel width must be at least
100 cycles. For unstable conditions it is desirable to transmit the first, second, and third
side frequencies. Thus, a 100-cycle band width will be suitable for speeds of 42 words
per minute. In actual practice 100-cycle bands have been found suitable for speeds up to
60 words per minute.
SECTION 19
FACSIMILE TRANSMISSION AND RECEPTION
BY
MAURICE ARTZT
ART. SCANNING SYSTEMS PAGE
1. Picture Elements 02
2. Scanners 03
3. Scanner Amplifiers 07
RECORDING SYSTEMS
4. Photographic Recording 11
5. Wet Electrolytic Recording 12
6. Dry Electrolytic Recording 13
7. Carbon-paper Recording IS
8. Comparison of Recording Methods 16
9. Recording Amplifiers 16
j^^ SYNCHRONIZING AND PHASING PAGB
10. Synchronizing 18
11. Phasing 21
TRANSMISSION CHARACTERISTICS
12. Wire Line Transmission 22
13. Radio Transmission 22
SPECIALIZED APPLICATIONS
14. Duplicators 23
15. Tape Facsimile 23
19-01
FACSIMILE TRANSMISSION AND RECEPTION
By Maurice Artzt
SCANNING SYSTEMS
Facsimile is defined to include all systems whereby a picture is broken into separate
picture elements, these elements being transmitted by some connecting means to a distant
recorder where they are reassembled into their original positions to form a copy of the
original. The word "picture" in the above statement includes also diagrams, typing,
handwriting, photographs, and any other form of printed or written material.
Three distinct operations are performed in the transmitting and recording of facsimiles:
first, the breaking up of the picture in some orderly manner into its separate elements of
varying shades, this process being called scanning; second, the transmitting of these ele-
ments to the recorder by means of signals arranged to represent the electrical equivalent of
these elements; third, the rebuilding of these signals by a recorder into a printed copy of the
original by a reversal of the scanning process.
A fourth part of a facsimile system, supplementary but very necessary, is a method of
synchronizing the recorder and scanner. The timing of the signals received must agree
exactly with the timing of the recorder, in phase as well as frequency, if the copy received is
to be undistorted.
In the following articles the terms used are in accordance with the definitions and stand-
ards as set up in 1942 by the Institute of Radio Engineers. See the first reference in the
Bibliography.
1. PICTURE ELEMENTS
In processing a picture by facsimile, the picture is resolved into dots, or picture elements,
similar to the small dots used in printing a picture in a newspaper or magazine. These dots
are obtained by "screening" in the printing process; they are obtained by scanning in
facsimile.
Halftones in newspaper work have from 60 to 120 dots, or picture elements, per inch,
whereas fine magazine printing may use as many as 250 dots per inch. In facsimile the
limits are of about the same order, almost all present facsimile systems using 100 dots (or
lines) per inch, as an average. Each picture element in a facsimile is sent as a separate
signal. If the number of dots is too high, the speed of transmission is very slow; if too few
elements are used, the detail will not be good enough. To send a picture of 100 dots per
inch requires as many as 10,000 separate signals per square inch of surface covered.
Figure 1 illustrates the difference to be expected between 50 and 100 lines per inch, when
the subject matter is ordinary typing. Some of the type would be unreadable if only 50
(a) 50 lines per inch (&) 100 lines per inch.
FIG. 1. Difference in Detail for 50 and 100 Lines per Inch for Typewritten Letters
lines per inch were used, as can be seen by the poor formation of the a. The 100-line-per-
inch detail, though not forming perfect letters, leaves no doubt as to their identity. In
commercial facsimile, letters from ordinary typewriters often comprise the original, and
approximately 100 lines per inch are necessary to insure readability.
Dots per inch and lines per inch are used interchangeably in the above paragraph, a
practice which is not always permissible. Some facsimile systems break the subject up into
19-02
SCANNERS
19-03
dots and send a separate signal for each dot, whether white, black, or gray. Others, how-
ever, break the sheet up into parallel lines and send signals only for the black areas as en-
countered. Each line is then a continuous signal, varying in intensity with the shading of
the original, and not made up of an exact number of picture elements as the dotted picture
is. The detail limits are the same in either case, and the maximum number of picture
elements per square inch is the same.
These picture elements, as observed by the scanner in the process of transmission, will be
of two general types, either of the simple black-and-white variety, such as typing, line
drawings, and so forth, or of the halftone variety, in which all shades of gray from white
to black may occur. Two separate types of scanners are not necessary, but the amplifier
equipment will sometimes be different. Any system capable of transmitting and recording
halftones will also operate properly on a purely black-and-white original, but the reverse is
not necessarily true.
2. SCANNERS
A facsimile scanning system includes an optical-mechanical scfl.Tm.er designed to project
a small spot of light on the subject copy, to gather the reflected or transmitted light from
-Driving motor
Guide rod
Drum
Phototube
Subject
copy
Drum shaft
• Lead screw gearing
FIG. 2. Scanner with Traversing Optical System
the subject into a phototube, and to bring all parts of the subject under this scanning spot
in some orderly manner. The signals generated in the phototube by the varying light values
reflected from the copy are then either amplified directly or processed in other ways to form
a usable electrical signal of a type suited for the particular application.
SCANNING METHODS. In the simplest form of scanning, regular lines are "ruled"
across the sheet by this spot of light at some particular number of lines per inch, and signals
are sent out representing each small area as it is encountered. The sheet is thus broken
19-04 FACSIMILE TRANSMISSION AND RECEPTION
into a number of narrow lines, all of the same width, and these lines are transmitted one
after another until the entire subject has been covered.
Scanning is generally done in only one direction and seldom back and forth. There are
two reasons for this : first a unidirectional scanner is simpler to construct and requires less
precision in gearing, and second the synchronizing system for back-and-forth scanning must
be far more accurate.
The simplest form of the scanner, and therefore the one most generally used, consists of a
drum upon which the original subject matter is wrapped, and an optical system arranged to
project a small spot of light on the surface of the paper. This spot is usually somewhat
smaller than the width of one scanning line. As the drum is revolved, the optical system is
moved relative to the drum the width of one scanning line for each revolution of the drum.
The entire subject is thus gradually passed under the scanning spot. See Fig. 2.
A phototube is arranged to pick up the light reflected from the surface of the paper, and
this light reaching the phototube will be varied in intensity by the different areas of black,
gray, and white that may be presented to view. The output of the phototube will be a
minimum for black and maximum for white and will represent electrically the scanning of
the copy. This phototube output is then applied to the input of the amplifier system.
All motions in the scanning process pictured in Fig. 2 are relative. Thus the optical sys-
tem may be rotated in place of the drum, and the motion along the axis may be made by
moving either the drum or the optical system relative to each other. All methods of
bringing about this relative motion have been used.
In one commercial type of scanner used for news picture transmission the drum is re-
volved and moved along the axis by a lead screw cut on its shaft, and the optical system is
stationary. See Fig. 3.
Motor
Drum shaft
half lead screw and half keyway
Nut on lead screw moves
rotating drum along shaft
Scanning
lenses
Drum with subject copy
FIG. 3. Scanner with Stationary Optics and Drum Feeding for Line Advance
As facsimile speeds have increased, the time required to load the subject on a drum has
become an increasingly greater proportion of the total time of transmission of the copy.
Various ingenious methods of loading and scanning have been devised to minimize this
loss of time. In one form of scanner designed for rapid loading, the subject is wrapped face
in around a transparent cylinder, and the optical system is rotated inside this cylinder.
See Fig. 4, By this method the scanning process does not have to be stopped to remove one
subject and put another in place. Thus the time to resynchronize and rephase for the next
subject is not lost, and the time between succeeding subjects is reduced.
In all scanners illustrated thus far the original must be of such size that it can be properly
chimped on the scanning drum. Thus copy width must be approximately the circumference
of the drum, minus the separation between clamps. The length is not so restricted and may
be anything up to the length of the drum. Another type of scanner in which width is not
restricted except as to a maximum value is shown in Fig. 5. The subject is placed face in
on a stationary transparent semicylinder and held there by a curtain (not shown) . Two
microscopes and light pick-up systems are rotated and traversed inside to scan the copy.
The two optical systems are set exactly 180° apart and in the same plane so that the signals
SCANNERS
19-05
Ssl
19-06 FACSIMILE TRANSMISSION AND RECEPTION
generated in the single phototube will be the equivalent of that from a single optical system
scanning a complete cylinder. With this scanner, unloading and reloading takes only a few
seconds as the copy is not clamped to hold it in place. As two optical systems are used the
shaft speed will be one-half that of an equivalent drum scanner.
In one other type of scanner used for telegraph service reloading with the next message is
accomplished, by dropping out the drum and copy when scanning is completed and re-
loading with another drum containing the next message from a hopper feed. This is done
automatically, and provision is made for accommodating a number of additional message-
carrying drums so that the messages follow one another in rapid succession.
SCANNER AMPLIFIERS
19-07
3. SCANNER AMPLIFIERS
The signals generated by the phototube will vary in amplitude with the shading on the
subject being scanned, and in frequency with the speed of the scanning spot and the kind of
subject copy. The highest frequency will be determined by the size of the smallest "dot"
it is expected to transmit; the lowest frequency will be zero or a direct current to represent
the large areas of white or black encountered in nearly all types of copy.
FREQUENCY SPECTRUM. The highest frequency is determined as follows: Take
the width of the smallest "dot" it is expected to transmit and rule a pattern of lines of this
width, separating them by the width of the dot. If the scanning is to be at 100 lines per inch
then these lines will be 0.01 in. in width, 50 to the inch, and separated by 0.01 in. Such a
pattern is shown in Fig. 6 A. The fundamental keying frequency of the phototube current
SCANNING
LINE
A. SCANNING PATTERN FOR FUNDAMENTAL KEYING
FREQUENCY GIVING GREATEST APERTURE DISTORTION
PHOTOTUBE
SIGNAL
OTUBE i Tl I I _ I I I
«" ILLmJ
f> . E , 2E Ps in fiT Sin 3mT , Sl'n 5g/T _ J
* - 2+Tf L I " 3 + 5 ]
B. PERFECT SIGNAL WITH APERTURE OF INFINITESIMAL WIDTH
PHOTOTUBE
SIGNAL
e
p _L.4E fsin <"T 3m3i*T sinSwT^ 1
c ~~ 2 If2 [ I 9 25 J
SIGNAL WITH APERTURE SAME WIDTH AS SCANNING UN£
PHOTOTUBE
SIGNAL
e
9 25
0. SIGNAL WITH APERTURE HALF THE WIDTH OF SCANNING
LINE
FIG. 6. Aperture Distortion of Signals
when scanning such a pattern would be 50 cycles per inch per second of spot speed. If the
scanning line were 9 in. long and the drum speed 100 rpm, the fundamental keying frequency
would be 50 x 9 x 100/60 = 750 cycles per second.
Higher harmonics of this fundamental keying frequency will be present as the subject
scanned is a square wave pattern. If the aperture of the scanner were infinitesimal in
width along the scanning line the phototube signal would be a square wave as ha Fig. QB
and would be very rich in harmonics as shown by the Fourier series under this figure. This
perfect signal is never realized hi practice, nor is it desirable, for the greatly increased band
width needed for transmission is not justified by the small increase in recorded detail over
that obtained by carrying only the fundamental keying frequency.
As the aperture is made wider the higher harmonics become less important. When the
aperture is the width of the scanning line the triangular wave in Fig. 6C is obtained. Here
the fundamental is 81 per cent and the third harmonic 9 per cent as compared to 127
and 42.5 per cent for the square wave. When the aperture is one-half the width of the
scanning line, a condition normally used in many scanners, the wave in Fig. 6D is obtained
where the fundamental is 115 per cent and the third harmonic 12.75 per cent. When using
this size of aperture very little difference can be noticed in the recorded copy whether the
19-08 FACSIMILE TRANSMISSION AND RECEPTION
third harmonic is carried or suppressed. For a more complete analysis of scanning see
Section 20, Television.
Almost all facsimile systems therefore carry only through the fundamental keying fre-
quency as the upper limit of the band necessary for transmission. In the illustration given
where this fundamental frequency was 750 cycles the signals from the phototube would
have a frequency spectrum of 0 to 750 cycles per second. This then is the input signal to
the scanner amplifier system, and, as the light reflected into the phototube is small, the
input signal is usually very low in amplitude.
TYPES OF SCANNER AMPLIFIER SIGNALS. The type of amplifier used in either
amplifying or processing the phototube signal will depend on the types of signal to be used
in transmission, and this in turn will be governed to some extent by the transmission me-
dium, whether it be wire line or radio. As the lower frequency limit is zero, ordinary
a-c coupled audio amplifiers cannot be used. In order to carry this zero frequency or d-c
component, the phototube signal is usually caused to modulate a carrier wave either in
amplitude or frequency. For transmission over wire lines the carrier frequency will be
chosen just high enough to carry the highest keying frequency. For radio transmission
the radio carrier itself can be amplitude or frequency modulated directly by the facsimile
signals, or a phone-type transmitter may be used and the facsimile modulation carried on an
audio subcarrier as for wire line transmission. Finally, for short distances over wire line
where no repeater stations or coupling transformers are used, a straight d-c amplifier may
be used between phototube and line. As it is difficult to maintain drift-free operation of a
d-c amplifier with sufficient amplification, this last method is seldom chosen.
The signals transmitted to the recorder may thus be of any one of the following types:
1. Subcarrier amplitude modulation (SCAM).
2. Subcarrier frequency modulation (SCFM).
3. Radio carrier amplitude modulation,
a. Direct without subcarrier.
6. With SCAM.
c. With SCFM.
4. Radio carrier frequency modulation,
o. Direct without subcarrier.
6. With SCAM.
c. With SCFM.
5. Direct-current signals.
For wire line transmission, signals of type 1 or 2 are commonly used, with 5 occasionally
on short control lines, for instance between scanner and radio transmitter. It is more usual,
however, if d-c signals are wanted to control a radio transmitter, to transmit signals of
types 1 or 2 on the control line and detect to obtain the d-c signals for control purposes.
For radio transmission over long distances signals of types 3c or 4a are normally used
as they give the most reliable results. For short radio circuits, as for instance local
coverage for broadcast facsimile service, 3c, 46, or 4c can be used on existing voice trans-
mitters.
Signals of types 3a and 36 are unreliable except for very short distances and have gen-
erally been supplanted by 3c if an a-m radio transmitter is used.
TYPES OF SCANNER AMPLIFIERS. It can be seen by the general usage of the
various signals that the two important types of amplifier systems will be either for am-
plitude-modulating a subcarrier or frequency-modulating a subcarrier. Where d-c signals
are required it is customary to use either one of these and then detect after amplifying to
the desired level.
SUBCARRIER AMPLITUDE MODULATION METHODS. There are three general
methods of obtaining signals of this type. First, from the standpoint of the length of time
it has been in use, is scanning with chopped light. If the light reaching the phototube is
made to nicker, either by modulating the light itself or by using a mechanical shutter or
chopper, the output voltage developed by the phototube will not be a direct current but a
pulsating voltage which may readily be amplified by an ordinary a-c amplifier.
The minimum frequency of chopping will be determined by the fundamental keying
frequency of the scanning process; the chopper frequency will be the carrier frequency and
must be high enough to carry the shortest "dot." In practice the chopper frequency is
usually made between 2 and 3 times the fundamental keying frequency, with 21/2 a good
average. In the previous example, with a keying frequency of 750 cycles per second, a
carrier or chopper frequency of about 1800 cycles would be used. The total bandwidth
transmitted would therefore be 1800 ± 750, or 1050 to 2550 cycles. This bandwidth is
narrow enough to be carried on regular voice telephone circuits and is so used for many news
picture transmissions.
SCANNER AMPLIFIERS
19-09
CONDENSER
LAMP
When an ordinary incandescent lamp is the light source, the chopper can be either a ro-
tating disk with holes or slots, or a ribbon or reed vibrating in a magnetic field. When a
glow-discharge lamp is the light source, such as used in some types of recorders, the light
can be modulated directly without me-
chanical shutters. The same lamp can
thus serve for scanning or for photo-
graphic recording on the same machine. , \ / -
Two other methods of obtaining a-m / \ //C-<MICRO SCOPE
signals are shown in Figs. 7 and 8. In • -J- \&^*Z. r-\64S PHOTOTUBE
the first the carrier is fed to the special
phototube in a balanced bridge circuit,
and a balance for minimum output
signal is obtained by means of the vari-
able resistor and capacitor with the
phototube dark. As light from the sub-
ject copy increases, the tone output of
the phototube increases and a true
modulation results. A simple audio
amplifier to build up the modulated
signals to the required level follows the
phototube circuit shown.
FIG. 7. Subcarrier Amplitude-modulated (SCAM) Sig-
nals Obtained by Balanced Phototube Circuit
In Fig. 8, the carrier is fed at 180° phase difference to the two screens of a pair of screen-
grid tubes. The plates are connected together so the outputs of the two tubes oppose each
other. By proper balancing of grid biases the output tone may be balanced to zero with
the phototube dark. As light to the phototube increases, the bridge is unbalanced and the
difference in output of the two tubes is obtained. With this circuit it is also possible to
balance for minimum signal with
maximum light for white on the
phototube, and the output tone
will then be a maximum for
black. Thus either positive or
negative modulation may be ob-
tained by shift of the balance ad-
justments.
In either of these circuits* the
frequency of the introduced car-
rier must be high enough to carry
the maximum keying frequency,
as explained previously with the
light chopper systems.
In this type of signal black is transmitted at one
FIG. 8.
Subcarrier Amplitude-modulated (SCAM) Signals
Obtained by Balanced Modulator
SUBCARRIER F-M METHODS.
frequency, white at some different frequency either higher or lower than that for black,
and intervening shades of gray at proportionate frequencies between these two limits. A
more complicated relationship exists between carrier, keying frequency, frequency swing,
and bandwidth required than with the a-m subcarrier. This is, of course, a true frequency
modulation and follows the same rules on sidebands as frequency modulation on a radio
carrier. (See Section 8 on frequency modulation.) However, it has been found that, with
a unity ratio of maximum keying frequency to the total frequency swing from black to
white, the usable bandwidth will be confined to about the same overall limits as the a-m
subcarrier with both upper and lower sidebands. Again, as with SCAM, the lowest carrier
frequency must be high enough to carry the shortest dot, so the low end of the carrier
swing should be at least 2 times the keying frequency. For the example with a keying
frequency of 750 cycles, the carrier may swing from 1500 to 2250 cycles in going from
white to black, and the total band spread (for all side frequencies greater than 10 per cent)
will be from 1125 to 2625 cycles. The mid frequency for middle gray will be 1875 cycles,
and only the first side frequency of ± 750 cycles need be carried.
This is only a deviation ratio of 0.5 at the highest keying frequency, but for all other pic-
ture frequencies the ratio is higher and for solid white backgrounds is practically infinite.
The signal-to-noise improvement over SCAM averages at least 12db for the usual subject
matter transmitted. Still greater improvement in signal-to-noise ratio would result from
increased swing, but at an increase in bandwidth that is not justified in most facsimile
services.
Two methods of obtaining this type of signal are in use. The first, shown in Fig. 9, con-
sists essentially of a beat oscillator with one of the oscillators being shifted over a small
percentage of its frequency by a reactance tube. As the light to the phototube increases,
19-10 FACSIMILE TRANSMISSION AND RECEPTION
the frequency of the variable oscillator will be lowered. The two oscillators are set at
sufficiently high frequencies so that the reactance tube can readily swing the required
number of cycles without changing amplitude. For the swing of 1500 cycles on white to
2250 cycles on black the fixed oscillator could be set at 100,000 cycles and the variable one
swung over the range from 102,250, with the phototube dark, to 101,500 cycles with the
phototube receiving maximum light for white.
SCANNER REACTANCE
TUBE
VARIABLE FIXED
OSCILLATOR OSCILLATOR
DETECTOR
FILTER
FiG/9. Use of Reactance Tube and Beat Oscillator to Obtain Sub carrier Frequency-modulated (SCFM)
Scanner Signals
A second method of obtaining SCFM signals directly, without heterodyning to obtain
the low frequencies, is shown in Fig. 10. A resistance-capacitance oscillator of the
180° phase shift type is varied In frequency directly by using a tube control system as a
variable resistor in one mesh of the phase shifting ladder network. When the control tube
has zero input (phototube dark) the bias is adjusted to set the low-frequency end of the
swing. As light to the phototube increases, the tube resistances decrease and the frequency
of the oscillator is raised. Input volume from the phototube is adjusted so that the high-
frequency end of the swing is just reached for white. When the proper network and tube
constants are chosen, a linear range as high as 2 to 1 in frequency may be obtained with
little change in amplitude.
OUTPUT
SCANNER VARIABLE
RESISTOR
RC OSCILLATOR
NETWORK
OSCILLATOR
FIG. 10. Use of Tube Control on RC Oscillator to Obtain Sub carrier Frequency-modulated (SCFM)
Scanner Signals
This circuit, when connected as shown, will give positive modulation, that is, an increase
in frequency for an increase in light. To obtain negative modulation a reversing tube
may be connected between the control grid and phototube, or the phototube may be
reversed and connected anode to grid, and cathode to a negative supply potential below
ground.
The changes in frequency with this circuit are very nearly instantaneous, because there
is little stored energy in the network. At the same time, the frequency stability is adequate
for the purpose.
It is sometimes necessary to use an existing scanning amplifier system having a-m output
and still transmit signals of the SCFM type. A converter is then used in which the SCAM
signals are rectified and filtered to obtain the original facsimile signals, and these are then
applied to the control grid of an SCFM generator of either of the above types.
PHOTOGRAPHIC RECORDING 19-11
RECORDING SYSTEMS
A perfect facsimile recorder will build up a copy of the signals exactly as received, adding
or subtracting nothing, and thus deliver a recording limited in detail only by the scanner
and intervening transmitting circuit. The finished picture will be almost identical in ap-
pearance to the original copy.
Of the many recording methods, the four most generally used will be described here:
photographic recording; wet electrolytic recording; dry electrolytic recording; and carbon-
paper recording. Each of these systems has advantages possessed by none of the others
and, therefore, will have particular uses to which it is the best adapted.
The length of the scanning line and the number of scanning lines per inch are generally
the same as for the scanner, but this agreement is not necessary. The recorder copy may
be made smaller or larger than the original by properly choosing the proportions of seanning-
line length to line advance. The product of the total length of the scanning line and the
number of lines per inch is called the index of cooperation; if this value is held constant, any
size recording may be made with all dimensions correctly proportioned to those of the
original copy. Thus, if the scanner has a total line length of 9 in. and is transmitting at
100 lines per inch, the index of cooperation would be 9 x 100 = 900. If it is desired to
receive this picture on a recorder having a scanning-line length of only 4.5 in., the line ad-
vance would be made 200 lines per inch, and the received copy would be exactly one-half
size.
Other than this index of cooperation, the other essential factor is the number of lines
transmitted per minute. This is (often) termed "strokes," and the "per minute," which
should be added, is understood. Thus the numbers 40-900 would signify a facsimile picture
having an index of cooperation of 900 and transmitted at the rate of 40 strokes per minute,
4. PHOTOGRAPHIC RECORDING
In recording photographically, the sensitized paper or film is generally wrapped on the
surface of a drum and is scanned by a small spot of light. The light spot is varied in in-
tensity or size to record the different values of picture density. It may be varied in several
ways — electrically, mechanically, or by means of polarization. In the electrically varied
light, a neon or other gas discharge lamp is modulated in intensity by the signals. With the
mechanical system, the light is steady, and varied either in intensity or size of spot by-
means of a vibrating shutter or diaphragm. In the polarized system, the Kerr cell is
interposed between the light source and the picture drum, and the light is polarized before
reaching the cell. The angle of polarization of the cell is changed by the picture signals,
allowing more or less light to reach the picture.
lm or Sensitized Paper
FIG. 1. Photographic Recorder, Using a Neon Lamp
The first method is more generally used in this country, and a simple recorder of this type
is shown in Fig. 1. Here the lamp is of the "point-source" type. An intense illumination
is produced in a small aperture within the lamp itself, and an image of this aperture is
projected onto the surface of the drum by a lens system. The spacings of the lamp and lens
19-12 FACSIMILE TRANSMISSION AND RECEPTION
system are so arranged that the aperture image is exactly the width of a scanning line. If
several values of line advance are to be used with the same optical system, a variable
diaphragm is introduced to regulate the size of the image to the proper value for the line
width desired.
The relative motions of the optical system and drum may be any of those used in the
simple drum scanner. Usually the drum is rotated while the optical system is gradually
advanced along its surface.
The second method of photographic recording involves "valving" the amount of light
reaching the paper from a steady light source, usually a tungsten-filament lamp. This can
be done by placing an oscillograph mirror and aperture in the light path, the position of the
mirror being varied electrically to change the area of the aperture exposed. As the amount
of light will be directly proportional to area, a smooth variation of light with signal is ob-
tained. Another method consists of placing a thin ribbon in the light path, just closing an
aperture. As the ribbon is twisted by the incoming signals, light is allowed to pass through
the aperture on both sides of the ribbon. This system produces a "variable width line"
type of recording similar in appearance to a zinc etching, or, if the aperture is placed at
90° to the scanning direction, it will produce lines of constant width but variable density.
In the third method of using polarized light, a Kerr cell is utilized to change the light
intensity. The optical system consists of two Nicol prisms placed between the light source
and the aperture. These prisms are polarized in the same plane and therefore pass light
through the system. The Kerr cell is interposed between the prisms, and applying signals
to its polarizing plates will change its light-polarizing properties. The amount of light
leaving the system is therefore controlled, and a true modulation of the light may be ob-
tained. This system has been used for a number of years in Europe.
The photographic system is far the most accurate in its ability to reproduce completely
the signals received and therefore is used in almost all commercial picture circuits. It has
one serious disadvantage, however, in that the received picture must be developed before
the results are known. The machine must be loaded and operated in the dark. In a fast
service this developing is quite a handicap, and the fact that the picture cannot be seen until
developed allows possible errors in the setting of the equipment to go unnoticed until the
full time of transmission and developing has elapsed.
Most picture circuits are operated at speeds of 6 to 10 square inches per minute, this
low speed usually being due to circuit limitations. With adequate light and sensitive films,
the photographic recorder is capable of speeds far in excess of this value.
5. WET ELECTROLYTIC RECORDING
Electrolytic recording is similar to photographic recording in chemical action but has the
advantage of being visible at once, or almost at once. It may or may not require some
form of processing to make the recording permanent, depending on the chemicals used.
The principle of operation is that certain chemicals turn very dark when an electric
current is passed through them. If a paper is saturated with such a chemical and scanned
by a stylus contact, it may be darkened by current at each signal for black and thus build
up the facsimile picture.
The common solutions are organic dyes, though silver or iron salts have sometimes been
used as in photography or blueprinting. Some of these solutions react very rapidly but
require high current density to bring about a dense enough black; others react with much
less current but require some form of washing or fixing to prevent fading.
One recording solution, which gives a dense black permanent recording, used a special
steel printer bar that is gradually worn away in the recording process. This chemical
process is capable of speeds up to 50 square inches per minute. The chemistry of the color
formation is given in U. S. patent 2,358,839. Another type of recording solution, which
uses a platinum bar that does not take part in the chemistry of recording, is given in U. S.
patent 2,306,471. The dye formed in this case may be any one of several of the azo dye
family, and is usually of a deep purple color. Speeds up to 160 square inches per minute
have been obtained with this type of solution.
A machine using a stylus would be a simple drum scanner with a dragging contact point
on the surface of the paper. Another form of electrolytic recorder requires a continuous
roll of supply paper and prints one picture after another without reloading. One form of
this continuous type of recorder is shown in Fig. 2.
Here the scanning is done by a combination of a printer bar and a helix on opposite sides
of the paper. The raised helix rotates at the same speed as the scanner drum, thus making
one complete turn in the length of a scanning line. The point of intersection of this helix
and bar will therefore travel across the paper once for each scanning line. Current for
DRY ELECTROLYTIC RECORDING
19-13
printing is passed between the helix and bar, through the paper. The bar is sprung slightly
and allowed to drag over the damp paper surface to secure good contact.
In this machine the paper must be moist to conduct the printer current and allow the
chemical reaction to take place. For the particular machine described, the paper is im-
pregnated with the chemicals and kept at the proper moisture content by storing in sealed
cans. The recorder itself is of moisture-tight construction so that the moisture in the paper
is retained until after printing.
In another form of electrolytic recorder a dry untreated paper is threaded through a
trough containing the recording chemicals before being fed between the helix and printer
bar. After printing it passes over a hot ironing roll to dry and smooth out the recording.
Paper feed roll
Slot for paper -
Intersection point
Helix
Motor
shaft
Moisture tight case
• Fixed printer bar
• Pretreated damp paper
FIG. 2. Recorder Using Wet Electrolytic Paper
The advantages of this type of recorder are its simplicity, its visible recording feature,
and the extremely high speeds of which it is capable. Recording speeds as high as 80 or 90
square inches per minute at 120 lines per inch definition are easily attained, allowing a
full-sized page of 8 1/2 by 11 inches to be recorded in 1 minute. Though the handling of
wet paper in the machine is awkward, this disadvantage is outweighed in many applications
by the speed of recording.
6. DRY ELECTROLYTIC RECORDING
Several dry electrolytic recording papers have been developed for message service fac-
simile recording: they are much easier to handle than the wet electrolytic papers, though
not capable of as high a recording speed. The best known of these, trade-named Tele-
deltos, has a light gray coating on a dense black paper base that has high electrical con-
ductivity. When current is passed from a small stylus through the paper the metallic
coating is burned away, leaving the black paper underneath exposed. The facsimile re-
cording is built up by scanning with a stylus and partially or completely burning the
coating where gray or black are to appear. See Fig. 3.
19-14 FACSIMILE TRANSMISSION AND RECEPTION
The advantages of this type of recording are that a permanent copy is produced with no
processing, the dry paper is easy to handle, and the recorder, with only a stylus and drum,
is mechanically simple. The disadvantages are that the contrast range of the finished copy
is reduced by the gray background, and the halftone scale is not as linear as the photo-
graphic or electrolytic recorders. These do not greatly affect its value for message service
where the subject matter is almost entirely made up of typing or handwriting.
CARBON-PAPER RECORDING 19-15
7. CARBON-PAPER RECORDING
The first carbon recorder consisted of a stylus dragging over carbon and white papers
wrapped on a^drum. The stylus was moved down to give pressure for black, and lifted for
white. This is a very simple form of recorder, but it has the disadvantage of the photo-
graphic recorder in that the picture is not visible until the drum is stopped and the carbon
paper removed. It has the advantages of cheapness and simplicity, and the picture re-
quires no processing to be permanent.
A later form of carbon recorder, illustrated in cross-section in Fig. 4, overcomes the dis-
advantage of invisible recording. Here the scanning is accomplished with a helix and
printer bar, as in the continuous electrolytic recorder. Carbon and white paper are fed
between the bar and helix, and after this are separated so that the surface of the white
Motor A k / , Intersection point
White papa-
feed roU
Carbon paper
take-up roll
^ Electro magnetic driver
FIG. 4. Continuous-feed Carbon Recorder
paper is visible only a few seconds after the printing process. The bar is not allowed to drag
the paper but is normally held away from it by an electromagnetic drive unit.
A signal for black depresses the bar, and a black dot is made by the pressure at the inter-
section of the bar and helix. The carbon paper is drawn over guides and wound up on a
take-up spindle. The white paper is fed by a knurled feed roll with a series of rubber idlers
held against it, similar to the paper feed of a typewriter.
Only one electromagnetic driver is shown for the printer bar. However, if wide paper is
used, more than one driver may be necessary and the separate units will be equally spaced
along the bar.
This method of recording is very simple, uses cheap paper, and prints a very good copy at
speeds up to 10 square inches per minute. It is quite reliable, and the complete copy, with
no processing necessary, is visible only a few seconds after recording. Its limitations are
also pronounced. The printer bar is necessarily heavier than a stylus, and therefore the
speed of recording is limited. Almost any carbon paper that may be used here will be soft
enough to smudge a little when rubbed in the fingers, the same as a carbon copy from a
typewriter. More mechanical accuracy is required in building this printing bar than in the
electrolytic recorder, as the bar and helix must be parallel to within a few thousandths of an
inch. The depressive motion of the bar is quite small, and, therefore, a little discrepancy in
lining up the bar and helix will result in failure of part of the paper to be printed to a full
black. Damping of the bar to eliminate "bouncing" and echo printing is somewhat of a
problem, but it can be solved by over-powering the printing mechanism and absorbing the
excess power in a damping arrangement on the bar itself.
One advantage mentioned separately here for emphasis is that this type of recorder may
be used to print more than one copy at a time. If the printer bar action is made sufficiently
powerful, several rolls of white and carbon paper may be threaded into the machine and a
number of copies of the facsimile made at the same time. As many as 8 separate copies of a
19-16
FACSIMILE TRANSMISSION AND RECEPTION
message have been made experimentally. Also the carbon paper may be of the "hecto-
graph" type and extra copies of the recording may then be made by the usual duplication
process of hectographing.
8. COMPARISON OF RECORDING METHODS
The recording method chosen for some particular service will depend on the quality of the
copy required, speed of transmission, cost of the recording paper, ease of operation, and
many other factors. In a news picture service, quality of the finished recording is most im-
portant, for the pictures are used as masters to make printing plates. Photographic re-
cording is therefore used for all these pictures, the other factors being considered of less
importance. Operating speeds are maintained as high as the wire lines or radio circuits will
permit, generally 9 or 10 square inches per minute with 100 lines per inch detail.
For message services, speed of transmission is the most important, with simplified equip-
ment able to run unattended as a next requirement. With somewhat limited bandwidths
available over wire lines, the high speed of the wet electrolytic process cannot be attained,
and the dry electrolytic process with its simpler recorder* structure more readily fits the
requirements. Operating speeds up to 30 or 40 square inches per minute can be maintained
with this type of recording, if the transmission band of the line will permit. The more
usual speed over most lines available for this type of service is 16 to 20 square inches per
minute.
The requirements for broadcast facsimile of flash news services are primarily for medium
speed, direct printing, and a minimum paper cost. Though the wet electrolytic recorder
does not use the cheapest paper, it meets the other requirements on speed and direct
printing. The copy appearance is pleasing, and the detail is adequate even at higher speeds
than those now contemplated. Such broadcast services will probably be most effective at
speeds of around 30 square inches per minute. Less than this is too slow, and higher speeds
will tend to increase apparatus and paper costs too greatly.
Carbon recording uses the cheapest paper and can run unattended for long periods of
time. However, it is the slowest of the recording methods, owing to the mechanical motion
required of the printer bar. Its highest operating speed at present is about 10 square inches
per minute, inadequate for most services but sufficient in some special instances where
speed is less important.
9. RECORDING AMPLIFIERS
The signals received for facsimile recording will usually be in the form of an a-m or f-m
tone. This may be either the original SCAM or SCFM tone transmitted over line or radio
by the scanner, or it may be one obtained by heterodyning in a radio transmission of direct
frequency modulation. If of the SCAM type, the signals will be applied directly to one of
the recording amplifiers described later. If of the SCFM type the signals must first be
changed into an equivalent SCAM signal by limiting and then passing the constant-
amplitude signal through a slope demodulating filter.
Such a converter unit is shown in Fig. 5. The incoming SCFM signal presumably will
have spurious amplitude modulation superimposed by fading if received by radio or
LIMITER FILTER DRIVER
LOW OR HIGH PASS
SLOPE FILTERS
FILTER CURVES
FIG. 5. Limiter Amplifier and Slope Demodulating Filters for SCFM-type Signals
changes in line transmission characteristics if received by wire line- Therefore it is first
passed through a limiter amplifier of several stages, so that the limiter output signal will, be
of constant amplitude over wide changes in input level. This constant-amplitude signal
then goes through either a low- or a high-pass filter, or both if pushpull output is desired.
RECORDING AMPLIFIERS
19-17
These filters are designed to have slow, straight cut off slopes so that the amplitude of the
output signals will vary linearly with frequency.
In the circuit shown the two end frequencies of the SCFM swing are labeled /i and /2 for
the white and black frequencies. If demodulated in the upper filter the output will be
greatest for /i and least for /a, while the output of the lower filter is the opposite. For un-
distorted demodulation these filter slopes must be linear beyond the band from /i to /2 by
SCAM ^ § o
RECORDER
+ B
THRESHOLD
FIG. 6. Printer Amplifier for Maximum Output Current with Minimum Signal Amplitude
the amount of the side frequency spread of the SCFM wave. For the previous example of a
swing of 1500 cycles for white to 2250 cycles for black, and band spread from 1125 to
2625 cycles, the filter slope must be linear over the entire range from 1125 to 2625 cycles.
The output of either slope filter will be the equivalent of an SCAM signal in amplitude
envelope and can be used in the printer amplifier in the same manner.
Four simplified diagrams of printer amplifiers to actuate the various types of recorders
are shown in Figs. 6, 7, 8, and 9. The first two are suitable for photographic recorders using
a glow discharge lamp to expose the film or paper. In each the SCAM signal is rectified and
RECORDER
" RECTIFIED ^
' THRESHOLD
FIG. 7. Printer Amplifier for Maximum Output Current with Maximum Signal Amplitude
filtered by a capacitor across the volume control to obtain the facsimile signals. The output
tube is then either driven to lower output current as signal amplitude increases, as in Fig. 6,
or to higher output current as amplitude increases, as in Fig. 7. The particular one used
will depend on the direction of modulation of the signal, and whether the drum is loaded
with film to make a negative or with photographic paper to make a positive copy.
For recorders using a pushpull magnetiqally driven printer, or driver units of a carbon
recorder, these two types of amplifiers may be combined, as in Fig. 8. As signal amplitude
increases, the upper output tube will be driven to lower current and the lower tube to higher
MIRROR
GALVANOMETER
SCAM^g
INPUT
RECTIFIERS VOLU
RECORDER
FIG. 8. Push-pull Printer Amplifier for Magnetically Driven Printer Systems
current. When properly adjusted true pushpull output is obtained, and the sum of the
two output tube currents will be constant. This constant-sum current can be used as shown
in the cathode return bias resistor to furnish the threshold bias required by the lower
output tube.
For electrolytic recorders of either the wet or dry type it is a good safety measure to run
the helix or recorder drum at ground potential. To accomplish this an amplifier such as in
Fig. 9 may be used. A pushpull power amplifier at cut-off bias amplifies the SCAM signals
19-18 FACSIMILE TRANSMISSION AND RECEPTION
to a power level sufficient for printing. This a-c signal is applied directly between the
ground drum and stylus for dry electrolytic recording, but it must be rectified and applied
between helix and bar in the proper polarity for most wet electrolytic printing processes. In
VWV— i
RECORDER
FIG. 9. Printer Amplifier for Either'Polarity of Electrolytic-type Recording. With non-polarity sensi-
tive papers, such as Teledeltos, the a-c output is used without rectification.
some of these the color forms on the anode side, in which case the bar is made positive with
respect to the helix; in others the color forms on the cathode side of the paper, and so
the bar is made negative.
SYNCHRONIZING AND PHASING
10. SYNCHRONIZING
In every facsimile system, it is necessary that the recorder follow the scanner over the
paper in order to produce an undistorted recording. The principle of synchronizing may be
better understood by refer-
ring to Fig. 1. For clarity
the picture elements are
shown much larger in pro-
portion than they really are.
As the scanner starts the
picture on element 1, the
recorder also starts on its
element 1. As succeeding
scanning lines are drawn, the
Scanner
FIG. 1.
Recorder
Synchronism of a Facsimile System
recorder must follow exactly, or the copy will be distorted by a misplacing of the elements.
Besides having the synchronizing correct, the recorder must be in "phase" with the
scanner, as illustrated in Fig. 2. Even though the two drums are rotating at exactly the
same speed, if they are not in phase the border of the picture will be misplaced. The re-
corder drum must start each scanning line at the same time the scanner is starting that
scanning line, or, as shown in Fig. 2C, the border will be somewhere between the two edges of
the paper instead of being exactly divided. Phasing and synchronizing become the same
problem only if the phasing line of the picture, or border, controls the speed of the recorder.
Where the synchronizing frequency is independent of the "phasing line," or of a much
higher frequency than that of the phasing line, the two problems are separate and must be
treated separately. This is generally the case in most commercial systems in use today.
A. Original in scanner B. Recorder in phase C. Recorder out of phase
FIG. 2. Phasing of a Facsimile Recorder
Before going into the means of synchronizing and phasing, the effect of imperfect syn-
chronizing should be shown, to illustrate the problem better. Figure 3 shows the effect of
an error in synchronizing on a unidirectional scanning system and on a back-and-forth
scanner. The error illustrated here is that the recorder is running faster than the scanner
by a very small percentage. In scanning the vertical line in A, the recorder gets farther
along its scanning line each time, moving the recorded line farther and farther to the right.
SYNCHRONIZING
19-19
The result, in a unidirectional system, is shown in B. In a back-and-forth scanning system,
the result is much more pronounced, alternate lines moving apart, as in C. The result, for
the recorder being too slow, would appear the same with this method of scanning, while
with the unidirectional system the line would have slanted down to the left instead of down
to the right.
The accuracy of the synchronizing may vary with the particular system. In commercial
work, the necessary accuracy is very high. In a system scanning at 60 strokes, 100 lines per
A. Original in scanner
B. Recorder fast, unidirec-
tional scanning
[C. Recorder fast, "back-
and-forth" scanning
FIG. 3. Recorder Not Perfectly Synchronized
inch, and each line of 9-in. length, the total length of scanning line per vertical inch of
paper is 900 in. In a picture of 10-in. length, this total scanning line length will then be
9000 in. A good copy will be made if the total drift in the border of the picture is not over
1/4 in. in this 10-in. length of picture. Thus, the synchronizing system must hold an ac-
curacy of 1/4 part in 9000, or 1 part in 36,000. It must hold this rate for the whole trans-
mitting time of nearly 17 minutes. Actually most commercial systems have synchronizing
equipment accurate to 1 part in 100,000 or better.
TUNING-FORK FREQUENCY STANDARD. In short-distance facsimile transmis-
sion, as for instance local coverage of a broadcast facsimile service, the same a-c power
supply is often available for both scanner and recorders. Synchronism is then simplified by
driving both scanner and recorders with ordinary synchronous motors connected to the
common supply. In long-distance transmission, or across the sea, this is not possible, and
synchronism is generally maintained by controlling the motors of both scanner and recorder
by accurate frequency standards. Such frequency standards usually take the form of very
accurate tuning forks that will hold a constant frequency to within 1 part in 100,000 or
better. Crystal standards could also be used, but, as the control frequency for the motor
is usually low, less dividing of frequency is required with a fork.
To hold the required accuracy, the fork is usually held at a fixed temperature by thermo-
stat control, or a temperature-compensated bimetallic type of fork is used. Figure 4 shows
one method of driving a tuning fork by using it as a resonant coupling circuit in a vacuum-
tube oscillator. By changing the driving power supplied to the fork, a vernier control on
I FREQUENCY
S-?YERN1ER
POWER AMPLIFIER
OR
THYRATRON INVERTER
FIG. 4. Fork Control of Synchronous Motor
its frequency is obtained. The fork frequency may be amplified by tubes or thyratron in-
verters to a power level sufficient to drive a synchronous motor directly, or it may be used
in other ways to control motor speed.
In one application, an 1800-cycle tuning fork is used both to supply carrier tone for an
SCAM signal and is also amplified to a power of about 10 watts to drive an 1800-cycle
synchronous motor. The synchronous motor is brought up to speed by a d-c motor, as it is
not self starting. In applications where a standard 60-cycle synchronous motor is used, the
fork frequency can be made 60 cycles, or divided down to 60 cycles from some higher
frequency.
MAGNETIC BRAKE SYNCHRONIZING. Another type of control circuit is shown
in Fig. 5. An induction motor, or other type of motor having good speed regulation, is
used to drive the recorder or scanner and is controlled to an exact speed by means of a
19-20 FACSIMILE TRANSMISSION AND RECEPTION
RECORDER TONE
(OR SCANNER) GENERATOR!
II5V 60**
FIG. 5. Magnetic Brake Synchronizing System
magnetic brake. A tone generator of the phonic wheel type is mounted on the motor shaft,
having the correct number of poles to generate a frequency equal to the fork frequency
at the correct motor speed. A phase comparison between this generated frequency and the
fork control frequency is
then used to vary the
brake current and make
the system lock into syn-
chronism with the fork.
A wave analysis of the
brake action is shown in
Fig. 6. The generated tone
and the fork tone are each
amplified and limited to
give the two square waves
e\ and e%, as in Fig. 6a.
These two waves are added
together algebraically in
the mixer tube to give the
waves shown in Fig. 66 and
are full-wave rectified to
give the waves in Fig. 6c.
The result is then the grid
voltage of the tubes sup-
plying the braking current,
shown in Fig. Qd.
Two conditions are illus-
trated. The waves on the
left side show the motor leading the fork by a small phase angle, and the pulses of brake
current are of full amplitude but narrow in time, so that the average brake current is
small. If the motor tries to speed up for any reason, such as an increase in line voltage or
lightening of the mechanical load, it
will advance in phase with respect
to the fork. The waves on the right
side illustrate how the brake current
pulses are increased in time width to
give a higher average brake current
that tends to slow down the motor.
The brake is thus turned full on, or
full off, by the square pulses, and the
correct average is obtained mechani-
cally rather than by smoothing these
pulses in a filter. Hunting is thereby
almost completely eliminated. As
the two waves are squared up before
comparing, the change in ratio of
time on to time off is a linear func-
tion with phase-angle changes of zero
to 180°.
As very effective brake action can
be obtained by passing the pulsating
direct current through the windings
of an ordinary induction motor, a
special design of brake is not neces-
sarily required. This system is es-
pecially well adapted for very high-
speed facsimile where motor powers
as high as 1/e hp are needed and con-
n
l
-i—
/"FC
RK e,
V MOTOR ]
ft
A'lr'*
!
T~
j
i~"
i
\
l
-4
1
i
-+
LIMITER OUTPUTS, e AND Ce
MIXER OUTPUT, (e,*e z)
rjDDUT TTTF
C. RECTIFIED SUM OF
FIG. 6. Brake Operation as Motor Goes from Small Phase
Lead on Fork to Large Lead
d. BRAKE CURRENT
trol must be at high frequency to
limit phase displacement with
changes in load or line voltage.
START-STOP SYNCHRONIZATION. The first methods used for facsimile synchro-
nization were generally of the start-stop type, and, although such a synchronizing system
is now practically obsolete for facsimile, it is still used on some forms of automatic tape
printers, such as the teletype.
In start-stop systems, the scanner is generally operated at a constant speed and has a
PHASING
19-21
"phasing line" of a considerable time length. During this phasing line interval, the recorder
will have finished its scanning line and stopped automatically. The scanner sends a pulse
at the start of the succeeding scanning line, and a clutch, or similar mechanical apparatus,
starts the recorder on the next scanning line. A governor-controlled motor, or some other
fairly accurate drive, is used to maintain the recorder at a constant speed for the duration
of each scanning line.
The chief merit of this system is that the errors in speed of the recorder are not accumu-
lated, each scanning line starting afresh. The greatest possible discrepancy in synchron-
izing, therefore, is the error in any one scanning line itself, and this can be made quite small.
The disadvantage is that the mechanics of such a system must be quite complicated, and a
definite starting pulse must be received or the entire scanning line is lost. The speed of the
entire system must, therefore, be quite slow to insure that these two factors do not interfere
with the picture. A complicated scanning system cannot be started instantaneously at a
high scanning speed, as allowances must be made for the inertia. Fading of the signal, if
received by radio, would cause such a system completely to miss whole scanning lines if
starting pulses were not received.
For use by line, such a system has advantages, as an ordinary governor will synchronize a
motor accurately enough for the purpose, and failure to receive a starting pulse is rare.
OTHER SYNCHRONIZING SYSTEMS. Certain recording systems require no syn-
chronizing at all, and such methods, sometimes used for cable transmission of pictures,
involve setting up a certain number of picture elements by machine, or by hand, and sending
a tape of this series of elements in numerical order. The recording is then assembled by
hand, usually requiring a competent artist to give the picture a lifelike appearance. This
method has been used for a number of years with great success over wire and cable. The
Bartholemew-McFarlane system or, in shorter terms, the "Bartlane" system is a variation
of this method.
The synchronizing frequency of the scanner is sometimes sent over the radio or wire line,
and an amplifier is used to build this signal up to a value where it is able to drive or control a
synchronous motor on the recorder. Such methods are satisfactory on line transmissions
and short radio circuits but cannot be depended on for long radio transmissions.
11. PHASING
The phasing of the recorder to the incoming signals can be accomplished either manually
or automatically. The simplest manual method is to throw the recorder out of syn-
chronism and let it drift until some indicator, such as a neon lamp fed by the phase signal
pulses, indicates in phase, and then to re-establish synchronism to hold this position.
In a simple automatic system, used on many news photo equipments, the recording drum
is driven through a clutch, and a projecting ear on the drum is arranged to engage against a
stop-pin having a magnetic release. At the start of the picture the drum is held in start
position by this pin, and the clutch slips. When the start phase signal is received the drum
is released and, being of low mechanical inertia, starts rotating almost immediately and in
phase. The stop-pin is locked out automatically when tripped, so the drum continues to
rotate for the duration of the picture transmission time. A phasing system suitable for a
continuous recorder is shown in Fig. 7. A phase signal is transmitted at the start of each
COMMUTATOR
CIRCUIT CLOSE£
EXCEPT DURING^
PHASE POSITION
MOTOR SUPPLY
POWER
PHASE SIGNAL •*•
DC PULSE INPUT
FIG. 7. Automatic Phasing of Continuous Recorder
scanning line, and this signal is selected out of the picture signals by frequency or amplitude
discrimination.
It is rectified and passed to the input circuit as a d-c pulse at the start of each line. In
series with this input is a commutator that is closed at all times except for a short gap at the
19-22 FACSIMILE TRANSMISSION AND RECEPTION
correct phase position. When the recorder is running in phase, this gap opens the circuit
for a slightly longer time than the duration of the phase pulse, so the tube receives no
signal. If the pulse arrives at any other time, it passes through the closed portion of the
commutator and causes the tube to draw a pulse of current to operate the relay. This
opens the motor circuit momentarily and causes it to drop synchronism. To insure the
relays staying open long enough for the motor to lose V2 or 1 cycle of synchronism, the con-
tacts B of the relay connect the capacitor from relay coil to ground, and the charge current of
the capacitor holds the relay in operating position for a fixed length of time. The resistor
across this capacitor is too high to pass enough current to hold the relay in, but it bleeds the
capacitor to zero charge between pulses. The motor is thus jogged out of synchronism
once for each pulse received in an out-of-phase position, and this process continues until the
correct phase position is reached, and the commutator again opens the pulse circuit at the
correct time.
TRANSMISSION CHARACTERISTICS
12. WIRE LINE TRANSMISSION
Transmission of facsimile signals by either wire line or radio puts more exacting require-
ments on the circuit than telephone or telegraph transmission. This is largely due to the
exact timing of the signals, which requires that delay equalization of a wire line be much
more precise than for telephone work. Any appreciable difference in arrival time at the
recorder of the high- and low-frequency components of the picture will show as transients
and ghosts that exaggerate the outlines of objects in the picture and may even make typing
unreadable. Accurate delay equalization is therefore required on all but short lines.
The amount of delay equalizing necessary is also directly affected by the speed of the
transmission and by the bandwidth required. For the previous example of a maximum
keying speed of 750 cycles, the shortest dot to be transmitted is 1/1500 second, or 0.667
millisecond. Any difference in delay equalization over the band of 1800 db 750 cycles, or
from 1050 to 2550 cycles, should not exceed a fraction of this 0.667 millisecond or noticeable
distortion will result. In this case, the line should be delay-equalized to =t 0.25 millisecond
over the 1050- to 2550-cycle bandwidth. In many long lines used for facsimile, this maxi-
mum delay error of db 0.25 millisecond, over a band of 1000 to 2600 cycles, is maintained.
If the speed of transmission were doubled, the maximum permissible delay error would be
halved and the bandwidth doubled at the same time. The problem of getting good enough
lines is therefore increasingly difficult as speed is increased.
This exactness of delay equalization can be compared to regular voice circuits where 10 or
even more milliseconds' delay difference does not appreciably affect quality of speech.
Where a-m signals are being used, the line must also be equalized for amplitude over the
transmission band, but this is usually an easier problem. Where SCFM signals are used the
amplitude characteristic of the line is relatively unimportant, but the delay characteristic
must be as good as for SCAM signals.
For short transmissions of less than 100 miles portable scanners are sometimes operated
into ordinary coin-box phones and over regular long-distance lines. This practice is satis-
factory in some cases, but distortion is much greater than over the specially equalized lines,
and picture quality is therefore lower.
13. RADIO TRANSMISSION
Radio transmission is beset with more difficulties than line transmission and, for long
distances, is generally slower. Many factors enter in long-distance radio transmissions,
such as fading, multipath delays, interference, echos, and other forms of distortion that
must be corrected for, or else the speed must be decreased until the particular distortion
present is reduced sufficiently to be no longer objectionable.
Rapid changes in transmission distance, due to varying heights of the ionized layers,
give the effect of varying delay times on wire lines and are the limiting factor on speed of
transmission. Some of the most pronounced effects can be eliminated by suitable directive
antennas with limited pick-up angles, to eliminate the next higher order of skip or hop.
When such antennas are used, and the proper choice of carrier frequency made for the dis-
tance, speeds up to 10 sq in. per minute are generally possible on circuits as long as New
York to London, and a speed of 6 sq in. per minute is very reliable.
In earlier radio facsimile systems, dot-halftoning was developed so that a keyed on-off
CW type of transmission might be used. Limiting the incoming signal then allowed most of
TAPE FACSIMILE 19-23
the results of fading to be removed. However, all present long-distance transmissions are
made either by using SCFM on regular voice transmitters, or direct frequency modulation,
or frequency shift of the radio carrier. The dot-halftone systems have therefore become
obsolete, and at the same time speeds have increased from 2 to 3 times that possible with the
dot systems. With either of these newer methods limiting can be done either at radio fre-
quency for frequency modulation or at audio frequency for SCFM and fading can be
largely removed.
For short distances, or when using ultra-high-frequency relaying, the speed is not so lim-
ited, for multipath troubles do not enter, and wide bands may be used.
SPECIALIZED APPLICATIONS
14. DUPLICATORS
Many applications of facsimile have been made that illustrate that it is not limited solely
to the transmission of pictures over long distances. The scanner and recorder can be
mounted on the same shaft and a duplicator, or copying machine, obtained. Two types of
facsimile duplicators are in use, each having definite advantages over other forms of du-
plicators in certain applications.
In one type of duplicator a wet electrolytic recorder is combined with a rapid-loading
type of scanner, such as shown in either Fig. 4, p. 5, or Fig. 5, p. 6. The speed of opera-
tion is very high, 85 sq in. per minute, and a full-sized letter page 8 1/2 by 11 in. is copied in
slightly over a minute, with 120 lines per inch detail. The wet paper passes over an ironing
roll after printing, and a finished dry copy is thus delivered.
As both scanner and recorder are rigidly coupled to the same driving motor, no synchro-
nizing or phasing is required. The amplifier system from phototube to printer becomes very
simple, as there is no transmission and reception problem over line or radio.
This type of duplicator is useful where only a few copies each of a large number of
originals are required. As reflected light is used the original may be opaque, entirely un-
suitable for blueprinting. It thus compares with photo-copying (though the cost of the
printing paper is less) but eliminates the necessity of developing and fixing.
MULTIFAX. In Multifax, a master mimeograph stencil is cut by facsimile methods
so that a large number of copies of the original may be made. Copy containing illustrations
and diagrams that would be almost impossible to make up by ordinary means can thus be
obtained in quantity, without going through more expensive printing processes.
The scanner and recorder are on the same shaft, as in Duplifax, to eliminate the need of
synchronizing and phasing. The stencil is clamped on a recording drum and cut by a stylus
which is vibrated at high frequency. While vibrating, the stylus is moved towards the
drum for black and delivers a large number of blows to the stencil to displace the wax. The
stylus is retracted for white so that it just misses touching the stencil. The vibrating stylus
has no tendency to drag out or tear the stencil, as it would if pressure only were applied, and
so much finer detail can be realized than with hand-cut stencils.
A full letter-sized master stencil can be prepared from the original in 10 or 15 minutes by
this method, about the time required for typing a stencil without illustrations. Another ad-
vantage is that the original is prepared on white paper, and printed diagrams or illustra-
tions may be pasted in place without being hand drawn on the stencil.
15. TAPE FACSIMILE
Tape facsimile systems are a special adaptation of facsimile in which the recording is printed
on a narrow slip similar to that used in news tickers. The scanning may be optical or me-
chanical, but the recorders for either type of scanning are usually of the helix and printer-
bar type, somewhat like a miniature version of the carbon recorder.
Where optical scanning is used, the message is typed, or handwritten, on the trans-
mitting tape, and this original copy then fed through a scanner similar to that shown in
Fig. 1. A spot of light is traversed across the width of the tape by the combination of a
rotating prism and a fixed system of three cylindrical lenses and one right-angle prism.
One stroke across the tape is obtained for each face of the prism that passes. These scan-
ning lines are very short, usually 1/4 to 1/2 in. The phototube signals generated by the re-
flected light are then used to obtain either SCAM or SCFM signals in the same manner as
in any page facsimile scanner amplifier.
19-24 FACSIMILE TRANSMISSION AND RECEPTION
For mechanical scanning the transmitter takes a form similar to a tape-teletype machine,
in which each letter is represented by a disk similar to an "Omnigraph" disk. Each disk
is a commutator and keys a series of signals that will form a facsimile image of that 'char-
acter when printed by the recorder. Operation of this form of tape scanner is then similar
'Phototube
Scanning prism
Pickup mirrors /rotating 600 rpm
Cylindrical lenses
Prism
Cylindrical lens
FIG. 1. Tape Facsimile Scanner
to that of a teletype machine, but with the output signals coded for facsimile recording
rather than for operating a typewriter type of receiver.
Either type of scanner will operate the tape recorder shown diagrammatically in Fig. 2.
The helix is very small for a scanning line as narrow as this, and it can be inked directly by
the ink roller shown instead of by using a slip of carbon paper to supply the coloring matter
as in the page type of recorders. Otherwise the recorder action is exactly the same as for
the page carbon recorder shown in Fig. 4, p. 15. Tape systems are built for message service
Felt inking
roller
Helix drum
600 rpm
Electromagnetic
driver
FIG. 2. Tape Facsimile Recorder
and do not need to have the fine detail usually required in a picture system. Whether op-
tical or mechanical scanning is used, the characters transmitted are large block type to re-
duce keying frequency and to get as large a number of words per minute as possible in a
narrow channel.
BIBLIOGRAPHY 19-25
The scanning-line length is very little greater than the height of a letter, so that there is
little waste time in margins. For instance, if 3/i6-in. block type is used, the scanning line
will be about 1/4 in. long. To transmit this type, the shortest dot necessary would be about
0.020 in., and a maximum number of cycles per scanning line would be 6. With the con-
stants of 60 lines per inch and 60 lines per second, 1 in. of tape per second is transmitted
with a keying speed of not over 360 cycles per second. This tape speed of 1 in. per sec will
represent about 60 words per minute.
While this band of 360 cycles for 60 words per minute is about 8 1/2 times that required
for the commercial automatic 7 unit codes, where 42 cycles (or bauds) per second represents
60 words per minute, this disadvantage is largely offset in instances where signals are poor,
or noise high. With tape facsimile, interference can obliterate a letter, but it cannot make
it print a wrong one.
BIBLIOGRAPHY
Standards on Facsimile, Definition of Terms, 1942, Supplement of Proc. I.R.E., Vol. 30, No. 7, Part IV.
Radio Facsimile, RCA Institutes Technical Press, 1938, pp. 112 to 128 contains a very complete bib-
liography of facsimile up to October 1938.
Mathes and Whitaker, Radio Facsimile by Subcarrier Frequency Modulation, RCA Rev., October
1939, pp. 131-154.
Artzt, M,, Frequency Modulation of RC Oscillators, Proc. I.R.E., July 1944, pp. 409-414.
Bliss, W. H., Subcarrier Frequency Modulation, Proc. I.R.K, August 1943, pp. 419-423.
Felch, E. P., Measuring Delay on Picture Transmission Circuits, Bell Lab. Rec., January 1936, pp.
154-157.
Hinshaw, F. A., Delay Equalizers for Telephotograph Transmission, Bell Lab. Rec., February 1936,
pp. 193-197.
Mertz, P., The Telephotograph Line, Bell Lab. Rec., February 1936, pp. 178-184.
Mertz and Pfleger, Irregularities in Broad-Band Wire Transmission Circuits, Bell Syst, Tech. J., Vol.
16, pp. 541-559 (October 1937).
Schulman, D., Facsimile Synchronizing Methods, Electronics, March 1946, pp. 131-133.
Wise and Coggeshall, The Handling of Telegrams in Facsimile, Proc. I.R.E., May 1941, pp. 237-242.
U, S. Patent 2,358,839, Iron Bar Wet Electrolytic Recording.
U. S. Patent 2,306,471, Axo Dye Wet Electrolytic Recording.
SECTION 20
TELEVISION
PRINCIPLES AND THEORY
1. Physiological Requirements ........... 02
2. Subdivision of Picture; Effect of Scan-
ning Rates ........................ 03
3. Resolution and Flicker Requirements;
Band Width ...................... 06
4. Pick-up Devices .... ................. 07
5. Picture Display Devices .............. 08
6. Synchronizing ....................... 11
7. The Video Signal .................... 13
8. The Composite Signal ................ 16
9. The Radio-frequency Signal ........... 17
10. Standards ............... . ........... 20
TELEVISION BROADCASTING
BY T. J. BtrzALSKi, A. L. HAMMERSCHMIDT, AND
F. J. SOMEBS
11. Lens Aperture Required .............. 21
12. Studio Camera Design ................ 22
13. Studio Equipment ................... 26
14. Gamma (Transfer Characteristic) ...... 29
15. Aperture Correction .................. 30
16. Film Pick-up ........................ 31
17. Master Control Position .............. 32
18. Pulse Measurements ................. 33
19. Overall Video System Response ........ 35
20. Television Field Pick-up Equipment ---- 36
ABT. PAGE
21. Relay of Television Signal 37
22. Transmitter Plant Terminal Equipment 41
TELEVISION RECEIVERS
BY W. F. BAILEY AND R. J. BBUNN
23. Antennas 47
24. R-f Circuits 47
25. Modulator and Local Oscillator 49
26. Picture I-f Amplifier 49
27. Picture Channel Second Detector 52
28. Video Amplifiers and Display 53
29. Noise Limiters 55
30. Sound Amplifiers 56
31. Synchronization 57
32. Scanning 59
33. Power Supply 62
OTHER FORMS OF TELEVISION
BY A. V. LOTJGHREN
34. Television Standards of Foreign Coun-
tries 64
35. Theater Television 64
36. Color Television 65
37. Binocular Television 67
38. Television for Special Services 67
39. Diplexing of Picture and Sound 67
20-01
TELEVISION
PRINCIPLES AND THEORY
By A. V. Loughren
Television is defined as "the electrical transmission and reception of transient visual
images." *
Television technique for monocular, monochrome pictures has developed sufficiently to
lead to adoption by the Federal Communications Commission of standards for broad-
casting.
1. PHYSIOLOGICAL REQUIREMENTS
The performance required of a television system is determined by physiological require-
ments which must be met for the performance to be acceptable. Section 14 discusses
these in detail. They vary from individual to individual, but generally acceptable design
values for the several quantities have been arrived at based on extensive tests. These
requirements include :
Resolution. An observer with good eyesight is able to resolve successive contrasting
objects individually subtending as little as 1 minute of arc. A square subtending 1 minute
of arc on a side corresponds to a solid angle of approximately 10~7 steradian. (Refer-
ences 1, 2, 3.)
Field of View.. A normal eye is capable instantaneously of critically observing a field
of the order of 0.001 steradian. Since the eye direction can be quickly and readily changed,
a much greater field than this is available within a very short interval of time. For sus-
tained viewing of images the viewing distance of four to eight times the picture height
chosen by most observers produces an image field of the order of 0.02 to 0.07 steradian.
Such a field is 200,000 to 700,000 times the minimum resolvable solid angle (reference 3).
Sharpness. Sharpness is the subjective quantity corresponding to the objective quan-
tity * 'resolution." Figure 1 shows the relation between sharpness and resolution; it in-
Relative Subject Sharpness in Laminal Units
5 i A 0 * » R
_- —
— • '
—
,^-««
^
^^
/
/
/
/
/
-16
/T
ousands
of Rgure
; of Confi
ision in t
ie Conve
ntional F
ield of VK
w
3 20 40 60 80 100 12
1 • I 1 1 !
0 140 160 10
43 2 1.5 1.0 0
7 as
Area of Figures of Conf us ion-Ste radians xlCT6
FIG. 1. Sharpness vs Resolution (from Baldwin, Ref. 4)
dicates that increasing the resolution by making the size of the figure of confusion less than
1.5 X 10 ~6 steradian increases the sharpness only slightly (reference 4).
*RMA.
20-02
SUBDIVISION OF PICTTJKE
20-03
Brightness. Because of its essentially logarithmic response and its ability to control
admitted light by means of the iris opening, the human eye is capable of observing objects
whose brightnesses lie within the range from 4 X 10 ~5 to 4000 ft-lamberts. It is found,
however, that satisfactory viewing requires restriction of this range. Under conditions
of low ambient illumination, highlight brightnesses as low as 1 ft-lambert are found ac-
ceptable; however, under conditions of normal artificial and natural lighting indoors, high-
light brightnesses as great as 200 ft-lamberts are desirable. Values of 10 to 100 ft-lam-
berts are suitable for design purposes.
Contrast. The total contrast range instantaneously perceptible to the eye is believed
to be about 40,000 : 1. However, reproductions exhibit contrast ranges from 10 : 1 for
rather unsatisfactory images to 200 : 1 for the best photographic transparencies. Tele-
vision pictures having a contrast range of 30 : 1 have been judged reasonably satisfactory.
Color. See Section 14 and references 5 and 25.
Depth. See Section 14.
Moving Objects. Ideally, reproduction of a picture of a moving object requires that
each elementary area of the picture change synchronously with the corresponding changes
in the original scene caused by the motion of the object. It is known, however, that the
resolution of the eye for moving objects is much poorer than for stationary objects. It is
consequently permissible to reproduce the picture at finite intervals rather than con-
tinuously. For most purposes the interval of 1/24 sec is short enough to leave with the
observer the illusion that motion is continuous rather than discontinuous.
Shape and Size of Picture. A rectangular shape with the width equal to four-thirds
of the height has been found generally acceptable. This ratio is defined as the aspect ratio.
The minimum acceptable size for reproduced pictures is believed to lie in the range
between 4 by 5.33 in. and 7 1/2 by 10 in. Smaller pictures produce fatigue within a short
time unless special devices are worn by the viewer. The maximum acceptable picture
size is determined primarily by the viewing distance available. For household use pic-
tures up to 15 by 20 in. are suitable, while for use in halls and theaters much larger ones
are appropriate.
2. SUBDIVISION OF PICTURE; EFFECT OF SCANNING RATES
Methods of transmitting and reproducing a television picture fall into two classes.
Both classes depend on the subdivision of the scene into a sufficiently large number of
elementary areas. In one class of system a separate transmission channel is provided
continuously for each element. The large number of elements required for a satisfactory
picture has shown systems of this class to be impracticable. In the other class, which all
present practical systems use, the elements are connected to a single transmission chan-
nel successively in an ordered sequence common to both transmitter and receiver. This
process is called scanning.
SCANNING. An area to be scanned is subdivided into elements each of which is
connected to the transmission channel periodically in some regular sequence. In its
simplest form the operation consists in starting at
the upper left-hand corner of the picture, traversing
successively the row of elements along the top of the
picture from left to right, following with a similar
traverse one element width lower, and continuing
this process until the bottom of the scanned area is
reached. A single traverse across the picture in one
direction is called a scanning line. The complete
scanning pattern is referred to as a raster. This
process is shown diagrammatically, for a picture
containing only a few scanning lines, in Fig. 2.
The electrical frequency components produced by
thus scanning a fixed image may be shown to con-
sist of: (1) a d-c component; (2) components at the
vertical scanning frequency and its harmonics; (3)
FIG. 2. Simple Raster
components at the horizontal scanning frequency and its harmonics; (4) components at
sum and difference frequencies of the above. Physically the d-c component represents
the average brightness of the image. The components at the vertical frequency and
its harmonics represent bands extending horizontally across the picture. The com-
ponents at the line frequency and its harmonics represent vertical bands. The compo-
nents at sum and difference frequencies represent inclined bands. If the picture changes
with time, side bands are added to some or all of these components (references 6 and 29) .
20-04
TELEVISION
Vertical Resolution. The scanning spot in the usual case is not rectangular nor does it
exhibit uniform effectiveness over its area. As a typical example of this, Fig. 3 shows the
distribution of light intensity over the scanning spot of a cathode-ray tube. If the spot
moves rapidly in one direction, forming a line, its effective distribution in the other direc-
tion assumes some such form as that shown in Fig. 4 at A. This figure also illustrates,
at B, the condition under which a flat field of illumination is produced by the overlap of
successive lines, and at C a line-to-line spacing which fails to produce a flat field. Similar
relations exist with respect to the scanning spot in the photosensitive device at the
transmitter.
The photo device at the transmitter should be adjusted to satisfy the flat-field criterion.
Failure to do this results in a type of distortion known as "beads," which is not susceptible
of any subsequent correction.
Vertical width of confusion, defined as the average width in the reproduced image of a
very narrow line appearing before the transmitter, positioned at a slight angle with re-
spect to the scanning lines, is equal to
V2 times the scanning-line pitch (ref-
erence 7).
Horizontal Resolution. If the scan-
ning spot of a pick-up device moves
horizontally across a vertical line of
negligible width, the resulting electri-
cal impulse describes the horizontal
characteristic of the spot. Typical
forms of this impulse are shown in
Fig. 5. The width of a rectangle hav-
ing the same maximum height, and
including the same area as the spot
characteristic (as shown dotted in
Fig. 56), is an approximate measure
of the duration of the impulse. Since
the spot is traveling at a fixed velocity,
the abscissa in Fig. 5 represents not
only time but also distance. It may,
for analysis, be transformed into
steady-state amplitude and phase
characteristics as functions of fre-
quency (for example, by means of the
J'
1
I
I
8.0
Distance Alpng Diameter— mm
FIG. 3, Distribution of Intensity across Scanning Spot
(After Zworykin, Proc, IJ2.2?., Dec., 1933)
Fourier integral theorem) . The effec-
tive band width may be expressed
approximately by the width of a rectangular area having the same maximum height
and same included area as the frequency characteristic. It may be shown that to a useful
approximation the effective spot width in seconds (or microseconds) is related to the ef-
fective band width in cycles (or megacycles) by the equation :
_
v.
(i)
where t is the time-duration of the equivalent rectangular electrical transient and fc is the
cutoff frequency of the equivalent rectangular frequency characteristic. A signal gen-
erated by a scanning spot moving across a narrow line as just described, transmitted elec-
trically and reproduced by a reproducing device, will have its frequency spectrum modified
both by the electrical circuits and by the equivalent transmission characteristic of the
spot of the reproducing device. These several characteristics may be multiplied together
to produce the overall transmission characteristic of the system. The corresponding ef-
fective horizontal width of confusion is then obtained by applying to this characteristic
the inverse transformation by means of the Fourier integral theorem. As an approxima-
tion, the effects of several sources of limitation on the frequency band width, connected in
cascade, on the effective overall band width, and on the duration of the shortest repro-
ducible impulse are given by the equations
(2)
and
fc VT^V
t •* vV + fe2 4- -
(3)
SUBDIVISION OF PICTURE
20-05
o
232
So long as the frequency characteristic^
or the transient impulse form reason-
ably well approximates the error func-
tion
the relations given above are close ap-
proximations (references 7 and 8) .
The scanning spot is usually symmet-
rical and thus exhibits no phase distor-
tion. The electrical circuits, however,
are potential sources of phase distortion.
Phase distortion affecting low-frequency
components of the reproduced picture
tends to alter the vertical or lateral
shading of the picture. Phase distortion
affecting high-frequency components-
tends to give the picture a "bas relief"
effect in which edges of objects in the-
image may be preceded or followed by
bright or dark outlines. Sharp cutoff
in the amplitude characteristic produces
"overshoots" superficially similar to
high-frequency phase distortion. The
two effects differ in that if a symmetrical
object is scanned the distortion due to
sharp amplitude cutoff will be itself'
symmetrical, whereas that due to phase-
distortion will be opposite in its char-
acter on the two sides of the image (ref-
erence 9).
FLICKER. Flicker is not inherent in
television. It is a consequence of the
use of scanning in conjunction with
picture display devices in which energy
is supplied to a given elementary area
of the display device for only a minute
fraction of the total time. The use of
such display devices with the scaiining.
sequence of Fig. 2. at a picture repeti-
a. Rectangular
Uniform Spot
r
b. Circular
Shaded Spot
by interlaced scanning.
FIG. 5. Electrical Impulse Produced by Scan-
ning a Narrow Vertical Line
tion rate of 25 or 30 per sec, produces
severe flicker at brightnesses even below
1 ft-lambert. Restriction of the maxi-
mum brightness to this level is not ac-
ceptable-
^ A major improvement is obtained
In this form of scanning, shown in Fig. 6, the vertical component
£
CO
20-06
TELEVISION
of velocity of the scanning spot is doubled as compared to that of Fig. 2 so that while the
spot crosses the picture from left to right it falls an interval equal to twice the distance
between scanning lines. If, therefore, the spot starts at the top center to trace line 1
after completing line 1 it goes to the left-hand side of the picture and starts line 3, con-
tinuing in this manner until it reaches the bottom right side of the picture. At this'point
the vertical retrace takes place and the spot returns to the top left of the picture and
starts to scan line 2, followed by lines 4, 6, etc., until the lower center of the picture is
reached. (For purposes of illustration the vertical retrace time is assumed to be very
small.) This method of operation has the conse-
quence that for an observer at such a distance that
he just fails to resolve individual scanning lines the
effective flicker frequency has been doubled; thus,
very much greater brightness is permissible without
any increase in the picture repetition rate. This
advantage is only slightly impaired when the ob-
server's distance is such that he can commence to
resolve individual scanning lines. The analogy be-
tween the practice of interlacing and the motion-
picture practice of interrupting the light at a rate
greater than the frame frequency should be noted.
In interlaced scanning the time required by a single
vertical traverse of the picture is no longer equal to
the time required to scan a complete picture. A single vertical scan is called a field;
a complete picture is called a frame. The customary variety of interlace thus has two
fields per frame. Higher orders of interlace have been proposed but have not found
widespread use.
It is desirable that the scanning processes, both horizontal and vertical, repeat exactly
from cycle to cycle. If the number of lines to a complete frame is an odd number, and a
frame consists of two fields, correct interlace and uniformity of repetition of the scanning
operation go hand in hand. This arrangement is called "odd-line interlace."
3. RESOLUTION AND FLICKER REQUIREMENTS; BAND WIDTH
In article 2 it was noted that the vertical width of confusion was equal to V2 times the
scanning-line pitch; hence
FIG. 6. Interlaced Scanning
where V is the picture height and n the number of useful scanning lines per picture.
was also noted that the horizontal width of confusion, in seconds, was
It
(1)
(5)
Wh = 2fc (6)
It is desirable that the horizontal and vertical widths of confusion be approximately equal.
Thus
Since
Wh = tv
where v is the horizontal spot velocity, it follows from eq. (1) that
whence
fc
2\/27
(8)
The number of useful lines in the complete picture, n, will be less than the total number
of line-periods in the picture time-interval, nf, by a factor a (usually 0.90 to 0.93) introduced
to provide time for the vertical return of the spot. The line-repetition rate or line-
scanning frequency, in cycles per second, is the product of the picture-repetition fre-
quency N and the total number of lines per picture, n\
If no time were allowed for horizontal return of the scanning spot from the right to the
left of the raster, the horizontal velocity would have the value
v = WNn' (9)
PICK-UP DEVICES 20-07
where W is the picture width. Retrace time must be provided, thus reducing the useful
portion of the line-period from unity to a fraction b, usually 0.82 to 0.85. The actual
velocity is then
WNn'
* - -g- (io)
Substituting this value in eq. (8)
_ nn'NW an^N W
fe — 7^ — ^~ X ~^ (11)
2\/2bV 2V26 V
and, since W/V, the aspect ratio, is 4/3,
fc = ~^- n*N (12)
If the picture is viewed from a distance equal to four times its height, the angular width
of confusion is found from eq. (4) to be
rrr V2
W* = J^7 radian (13)
while the corresponding square solid angle is
1
S ~ — ^~~^> steradian (14)
In article 1 it was stated that the figure of confusion should not exceed 1.5 X 10"6
steradian. However, the method of defining the boundaries of the figure, in the study
there referred to (reference 4) , differed from that of article 2 sufficiently to require intro-
duction of the factor 1/1.9 when this figure is applied to the preceding analysis. Using
the resulting value of 0.8 X 10 ~* steradian, and choosing the value 0.90 for a, eq. (14)
yields the value
ri — 439 lines per picture
The American television standards have been set at 525 lines per picture, thus more than
meeting the resolution requirement in the vertical direction.
The vertical repetition rate must be at least 25 and preferably 30 per second for the com-
plete picture in order to minimize flicker, even with interlaced scanning. It is advantageous
to make the rate an integral submultiple of the power supply frequency, to eliminate dis-
turbance of interlace by stray fields; a vertical rate of 30 per second is therefore chosen.
The corresponding line frequency is 30 times 525, or 15,750 cycles per second.
The effective cutoff frequency, as defined in article 2, is obtained by substituting in
eq. (12) the values a = 0.90, b = 0.84, nf = 525, N = 30. Thus
fe = 0.505n'2JV = 4.1S Me
With a frequency band including components up to 4 or 4.5 Me, the gradual cutoff re-
quired to avoid severe "overshoots" (and usually obtained automatically as a consequence
of scanning spot distributions) results in an effective band width which rarely exceeds 3
Me (reference 7). The condition of equal vertical and horizontal widths of confusion
(eq. [71) is thus not usually obtained; moderate departures from this condition are known
to be of only minor importance (reference 4) .
4. PICK-UP DEVICES
Early work on television employed mechanical scanning of the object or scene to be
televised. The optical system focused an image on a plane at which a disk provided with
apertures spaced about its periphery was interposed. A single rotation of the disk pro-
duced one complete scan of the image. The photoresponsive device located behind the
disk responded instantaneously to the light transmitted by the apertures as they suc-
cessively traversed the image. In a modification of this arrangement the scanning process
was applied to the light which illuminated the object. This modification reduced the
total amount of light incident on the subject, and the accompanying heat, very con-
siderably.
Analysis of these mechanical scanning methods shows that the light incident upon the
photoresponsive device is inversely proportional to the number of picture elements, and
that, for an acceptable number of elements in the picture, it is not practicable to increase
the scene lighting and the pick-up lens size sufficiently to produce a useful signal-to-noise
ratio (reference 26). The limitation inherent in mechanical pick-up systems encouraged
20-08 TELEVISION
the development of photo responsive devices capable of storing light energy over the
entire scanning period, thus permitting an improvement of several orders of magnitude
in the signal-to-noise ratio. These devices are described in Section 15.
5. PICTURE DISPLAY DEVICES
Early picture display devices employed a light source of instantaneously controllable
intensity (such as a crater-type glow-discharge lamp or a high-intensity arc whose light
output was modulated by a Kerr cell) in conjunction with a mechanical scanning device
similar to that described in connection with the preceding article. With arrangements
of this sort each picture element is illuminated for a time interval corresponding to its
own duration.
The average illumination of a picture element at the viewing screen is equal to the il-
lumination intensity during the picture element divided by the ratio of frame duration to
picture element duration. A typical value for this ratio is 300,000. In consequence of
this factor, and the limited intrinsic brightnesses of convenient light sources, mechanical
scanning systems as heretofore proposed have been largely supplanted by electronic scan-
ning using cathode-ray tubes (reference 2) .
In a modification of a mechanically scanned television reproducer, Scophony developed
a method of storing the light-modulation information in a liquid cell in such fashion that
an individual picture element could be illuminated for a period many times the element's
own duration. Practical difficulties have prevented widespread use of this arrangement
(references 10, 11, 12, and 13).
In a cathode-ray tube the instantaneous power concentration in the scanning spot may
reach values of 10 to 1000 kw per sq in. Efficiencies of fluorescent materials in converting
from electrical to luminous energy lie in the range of 5 to 10 per cent. On this basis,
average highlight brightnesses of a few thousand foot-lamberts are possible. The cathode-
ray tube has, therefore, become the accepted television picture-reproducing device. Cath-
ode-ray tubes are described more fully in Section 15.
Electronic control of the opacity or alternatively the light-reflection coefficient of a
surface has been employed for certain special purposes. In one form the effect of an in-
jected electron in producing opacity in a transparent alkali halide crystal is employed.
In another arrangement a layer of flakelike particles such as graphite, suspended in a
fluid, is used; in the absence of electric field the particles exhibit random orientation and
thus prevent light transmission, but an applied electric field makes the orientation orderly
-and permits light transmission in the direction of the field (references 14, 15, and 16).
SCANNING CIRCUITS FOR CATHODE-RAY DEVICES. The electron beam of
the cathode-ray tube may be deflected by either electric or magnetic field. Both fields
involve the storage of energy in the deflection space within the tube and incidentally in
the external circuits.
Wave forms for a deflecting field are shown in Fig. 7. Curve A shows an ideal form.
Curve B shows a departure from the ideal form introduced to permit a finite retrace time
and thus avoid the necessity for han-
dling unreasonably excessive currents
or voltages in the deflection circuits
during the retrace intervals. Curve C
shows a typical practical curve in which
the form of variation is modified from
that of curve B to eliminate the discon-
tinuities of slope exhibited by curve B
and thus reduce the number of harmon-
ics which must be faithfully transmitted
to the deflecting circuit.
For faithful reproduction it is essen-
tial that the scanning wave -have the
same form in both the pick-up device
and the reproducing device. It has not
Time — ^-
FIG. 7. Scanning Field Wave Forms. A. Ideal Re-
quirement. B. Modification for Finite Retrace Time.
C, Modification for Finite Bandwidth.
been found practicable to control with sufficient accuracy the wave form of the deflecting
field during the retrace interval. It is essential, therefore, that no attempt be made to
transmit picture information during this interval. Means are customarily provided for
preventing the appearance of the reproducing screen from being affected by signal potentials
^hiring the retrace.
SCANNING CIRCUITS FOR ELECTROSTATIC DEFLECTION. Figure 8 shows a
typical circuit for producing electrostatic deflection voltages. Oscillator tube V-l is
PICTUEE DISPLAY DEVICES
20-09
here shown as a blocking oscillator. Other forms such as multivibrators and thyratrons
may also be used. The oscillator acts periodically to discharge capacitor Ci. The ca-
pacitor is then charged through R\ until the voltage at the oscillator anode rises to a point
where, in conjunction with any voltage which may be applied on the grid, oscillation is
again produced, thus again discharging Ci. The voltage variation with time on Ci during
the trace portion of the period is, of course, exponential. It is essential, therefore, that
the amplitude at this point be kept small enough to preserve a good approximation to
FIG. 8. Electrostatic Deflection Circuit
linearity. The amplifier tube Vz and phase inverter tube Vz amplify the voltage appear-
ing across C\ to the required level and provide the usually necessary outputs of opposite
polarities. In choosing the values of components care must be taken that the capacitors
C2, Cs, C4, and Cs do not introduce excessive phase shift for the fundamental frequency
component. A total shift of 3° is a useful upper limit. By care in the choice of com-
ponent values the circuit may be made to work down to frequencies much lower than the
normal television field frequency of 60 cycles; it may also be used readily at frequencies
at least ten times higher than the normal line-scanning frequency of 15.7 kc.
A simpler circuit which is useful for scanning frequencies of the same order as television
line frequencies is shown in Fig, 9. In this circuit capacitors C\ and Cz are charged from.
FIG. 9. Electrostatic Deflection Circuit
the power supply during the trace period through the reactor Li, La. While this charging
current is oscillatory, the choice of a resonant frequency less than one-tenth the scanning
frequency for the circuit consisting of the two reactor windings and two capacitors in
series results in the use of only the linear central portion of the oscillatory cycle. When
the voltage appearing across Ci and Cz is great enough, tube Vi goes into oscillation draw-
ing a heavy current and discharging the pair of capacitors. If the equivalent series re-
sistance of Vi is sufficiently low, this discharge will be oscillatory and will last for one-half
cycle at a frequency determined by the apparent inductance of the primary of trans-
former T and the capacitance of capacitors Ci and <72. (Insufficient leakage inductance
in T makes the retrace time unnecessarily short and the peak current and dissipation in
20-10
TELEVISION
Vi excessive.) The potential difference between the opposite ends of Ci and C2 reverses
during this discharge and rises to a negative value which may be a considerable fraction
of the voltage on the capacitors before Vi began to conduct. With the cessation of con-
duction in Vi, Ci and C2 are again charged through I/i, Z/2, and the cycle repeats.
CIRCUITS FOR MAGNETIC SCANNING. In the magnetic scanning cycle the cur-
rent in the coil by which the magnetic field is produced is zero at the midpoint of the
scanning trace. During the latter half of the trace the current is built up under control
of a vacuum tube to the value required to produce
the full deflection. The flow of current through
the vacuum tube is then interrupted, and the
scanning current continues to flow in the coil,
charging the distributed capacitance which is in
shunt with the coil until the current vanishes.
The distributed capacitance is now charged to a
high potential; it discharges back into the coil,
producing a current of opposite polarity to that
which previously flowed. When the potential
energy stored in the distributed capacitance has
been transferred completely back to the coil, the
next scanning-line trace starts; the flow of coil
current is permitted to continue through a vacuum
tube in order to cause the current to decrease
linearly to zero value at the midpoint of the trace.
In this cycle energy is supplied to the circuit dur-
ing the latter half of each trace, a half-period of
free oscillation takes place during the retrace, and
the energy is then dissipated during the first half
of the succeeding trace. These relations are
shown on an ideal basis in Fig. 10. It is necessary,
of course, that the resonant half-period of the free
oscillation not exceed the permissible retrace time.
The energy required in the magnetic field (with-
in the tube) to deflect a cathode-ray tube fully is
a function of accelerating voltage and deflection
angle primarily. Typical tubes require amounts
of energy between 30 and 300 micro joules. These
amounts of energy must be provided and dissi-
pated during each scanning cycle. Thus, for a
type 10BP4 cathode-ray tube requiring about 300
microjoules for horizontal deflection and a hori-
zontal deflection frequency of 15,750 the power
which must be delivered by the scanning circuit
within the tube is 4.8 watts.
A typical line-frequency magnetic scanning cir-
cuit is shown in Fig. 11.
A step-down transformer is interposed between
the energy supply tube V\ and the scanning coil
or yoke K, to decrease the effective distributed
capacitance of the circuit, thus assisting to obtain
suitably short retrace time. The wave-form dia-
grams of the figure, which are corrected for the
effect of the transformer ratio, show the current
gradually increasing in tube V\ during the trace and terminating abruptly at retrace. Dur-
ing this same period the current in tube Vz rises abruptly to a maximum value and decreases
smoothly during the rest of the trace. The analogy between these two current wave
forms and the corresponding forms in a class AB amplifier should be noted. Tube Vs
provides the feedback connection for self-oscillation.
The circuit is arranged to make use of the energy returned by the yoke Y during the
first half of the trace. This energy is stored in capacitor Ci; the voltage thus developed
across Ci is used to augment the anode supply voltage for tube Vi. This is called the
"bootstrap" connection.
It is usually necessary, for line-frequency scanning, to use a relatively low inductance
in the yoke. The current is therefore relatively high and may reach peak values of 0.1
to 1:0 amp. Relatively large direct currents (0.01 to 0.20 amp) are consequently required
to correct any incidental decentering of the raster. The circuit of Fig. 11 is therefore
FIG. 10.
Energy Relations in Magnetic
Scanning
SYNCHRONIZING
20-11
designed to permit the full B supply current of the receiver to flow through the centering
control.
Overall efficiency of the circuit of Fig. 11 may reach a value of 15 per cent. Delivery
of 5 watts to the magnetic field within the tube thus requires at least 30 watts of d-c power
(reference 80).
The power required for the relatively slow vertical scanning is very much smaller than
that for horizontal scanning. A typical circuit is described in article 32 of this section.
-JH
Synchronizing
e-f
!FiG. 11. Magnetic Scanning Circuit
KEYSTONE CORRECTION. When the electron beam in its undeflected position
does not strike its target at a right angle the shape of the raster produced by uniform de-
flecting fields will be a keystone. Circuit arrangements which modulate one of the scan-
ning generators by a signal derived from the other are required to produce a rectangular
raster under these conditions. Application for these is found in the Iconoscope type of
camera tube and in certain forms of picture tubes (reference 81).
6. SYNCHRONIZING
In television practice the picture information is generated in an orderly sequence. The
picture display device must display this information in the same sequence if the original
picture is to be reproduced. It is necessary, therefore, that information to synchronize
the scanning operations of the display device be furnished with the picture information
and that this information be subject to delays in transmission identical to those experienced
by the picture information. Synchronizing signals are, therefore, included with the
picture signals. , . , .
There are two ways in which scanning devices may be synchronized. In the simpler of
these the synchronizing signal has essentially a pulse form and is applied to the scanning
device in such fashion as to terminate the scanning trace and initiate the retrace. This
action takes place at a speed limited only by the transient response of the scanning oscil-
lator itself This method of operation has the advantage of simplicity but the disad-
vantage that the scanning cycle may be mistimed and the picture consequently distorted
by either: (1.) a noise impulse tripping the oscillator prematurely; (2) loss of a synchronizing
pulse due to a temporary blocking of the signal channel by noise, or (3) the combination
of random noise components with the synchronizing pulse to produce random phase vari-
ation of the leading edge of the pulse. _ .
The alternative synchronizing method is to apply the synchronizing signal and a signal
derived from the scanning device to a phase comparison circuit whose output voltage
controls the frequency of the scanning device. If the synchronizing pukes are uniformly
spaced and the scanning device is itself stable in frequency, the phase control may be made
slow acting, thus effectively decreasing the band width of the synchronmng signal channel
and reducing its susceptibility to noise interference by several orders of magnitude (refer-
ence 17).
20-12
TELEVISION
C
a
s
•8
o
^
I
I
< <
<M
QQ
O
CSJ
O
THE VIDEO SIGNAL
20-13
L
Separate synchronizing signals are required for the two directions of scanning With
interlaced scanning it is essential that these signals be readily separable one from the other
in a receiver. The form of composite synchronizing signal which has been adopted to
meet these requirements is shown in Fig. 12. In line AI of Fig. 12 the last three line-
synchronizing pulses preceding the vertical retrace interval appear at the left, followed
by six equalizing pulses, six field synchronizing or "broad" pulses, and six more equalizing
pulses. Transmission of normal Line pulses is then resumed, to continue until the next
field retrace interval, shown at A2. The traces AI and A2 are separated in time by exactly
one field period; in consequence of the use of "odd-line interlace," the line pulses in AI and
A2 are one-half line period out of phase. The line-frequency signals may be separated
from the composite signal by differ-
entiation, as shown at BI, B&; the f 1 It-
arrows here represent the times at
which the line oscillator should
"fire"; at each of these, a synchro-
nizing signal is provided. The field
frequency signals may be separated
by integration, with the results
shown at Ci, Cj. It is a characteris-
tic of an integrating circuit that it
"remembers." For this reason the
interval immediately preceding the
vertical synchronizing signal con-
tains horizontal synchronizing sig-
nals at twice the normal repetition
rate. By this means the time in-
tervals immediately preceding the
vertical synchronizing pulses in the
two fields are made identical. The
line synchronizing pulses are reduced
to half their normal duration during
this period so that their integrated
value will be no greater than that
of line pulses of normal duration
and normal repetition rate. These
equalizing pulses also appear for a
0 ^
r i =
+B
> ' o
-a
Differentiating C
¥•
ircuit for Line; RC = 2. usec.
Integrating Circuit tor Field; R=!00k ohms,
C« 0.005 jif.
FIG. 13. Synchronizing Signal Selection
short interval following the vertical synchronizing signal to insure that during the entire
interval in which the vertical scanning device is sensitive to synchronizing signals those
signals will be alike in both fields.
The diagrams of Fig, 13 illustrate differentiating and integrating circuits to perform
the separations shown, in Fig. 12.
7. THE VIDEO SIGNAL
The video signal is generated by a pick-up tube as described in Section 15. The output
of this device usually requires amplification to raise it to usable level and may, in addition,
require processing to remove from the signal certain spurious components which are not
properly a part of the signal. Its direct component must either be transmitted faith-
fully with the same gain as other components or be reinserted by either manual or auto-
matic means after amplification has taken place.
Figure 14 shows a test pattern used for testing television systems and the oscillogram
of a single scanning line of that pattern. The oscillogram was taken at a point in the
transmission system where all spurious components had been eliminated. The corre-
spondence between elements of the picture and elements of the oscillogram is shown.
TRANSMISSION OF THE D-C COMPONENT. It is theoretically possible to trans-
mit and amplify the d-c component along with the other components of the video signal.
In practice, however, this is frequently found to be inconvenient. A satisfactory alter-
native, known as "d-c reinsertion," may be followed once the black level of the signal has
been established. In this alternative practice the recurring black intervals are used to
provide an a-c carrier of the d-c component. This practice is illustrated in its simplest
form in the two-stage amplifier of Fig. 15. The blocking capacitor Ci prevents transmis-
sion of the d-c component from the anode circuit of Vi to the grid of "V& The video signal
is applied to the grid of Yi with positive polarity, that is, with an increase in object bright-
ness represented by a change of signal potential in the positive direction. The black level,
20-14
TELEVISION
therefore, represents the most negative portion of the signal. The signal polarity is re-
versed in the anode circuit of Vi so that at this point the black level is the most positive
portion of the signal. The diode Vz is connected to conduct on the positive portion of
FIG. 14. Television Test Pattern and Sample Line Wave Form. Test pattern (copyrighted by Radio
Corp. of America). Wave form of single line as shown.
the signal reaching it. (The grid-to-cathode conductance of Vz shows a similar character-
istic.) Current flowing through the diode in response to the black intervals of the signal
establishes such a charge on Ci as to reduce the flow of current through the diode to a value
just sufficient to make up for the leakage from the condenser through Rit If the effective
resistance of the charging path (including the series resistance of the diode and the re-
sistance of Rz) is small, the amount by which the diode anode is positive with respect to its
FIG. 15. D-c Reinsertion Circuit
cathode, during the black intervals, will be a negligible fraction of the total signal poten-
tial. The black intervals of the signal will, therefore, be held at substantially the poten-
tial of the diode cathode, and the gray and white portions will extend negatively from this
potential in their appropriate amounts.
THE VIDEO SIGNAL
20-15
2g
§ i § i
*+••!• +
-^ m-1
T i T
> 2
1
(apouv)
I
s
8
CJ
•f-
(apouy)
0>
20-16
TELEVISION
Signal
Input
Figure 16 shows the performance of the circuit of Fig. 15 with two different signals.
Signal A has a little white, but mostly dark gray and black, while signal B is all white
except for a brief black interval. The effectiveness of the reinsertion action is shown by
the substantial agreement in black levels for both signals, at the grid and also at the anode
of 72. The curves shown for the performance at Vz when the diode is replaced by a fixed
bias show the much greater range of voltages
which tube Vi must handle without distortion,
if d-c reinsertion is not practiced*
Because of the high impedance of diodes at
the low currents they are called upon to handle
in the circuit of Fig. 15, the accuracy with
which the black level is maintained is some-
what imperfect. When more accurate per-
formance is required, a more elaborate
arrangement known as a clamp circuit may be
used in place of the diode Vz and resistor RI of
Fig. 15. In a clamp circuit, an external source
applies power to a network of diodes, producing
considerable currents and low diode imped-
ances. The network is balanced so that any
deviation of the signal potential from the
potential of a reference point during the flow
of current from the external source is corrected
by a small unbalance in the currents in the
branches of the circuit. Figure 17 shows one
form of clamp circuit. Clamp circuits differ
from the circuit Fig. 15 in that (a) they are
Reference
' Potential
JUL'
^Energizing
Signal
FIG. 17. Clamp Circuit
capable of conduction in both directions; (6) in consequence of this they must be energized
•nly during appropriate time intervals. See also reference 27 and 84.
8. THE COMPOSITE SIGNAL
la the, design of television systems provision must be made for the transmission of these
four signals: (a) video signal; (6) horizontal synchronizing signal; (c) vertical synchronizing
signal; and (d) sound signal.
The system may be designed to transmit all four of these from separate transmitters.
Alternatively, two or more may be combined and transmitted by a single transmitter.
The combination of the picture signal and the two synchronizing signals in a single trans-
mission has been recognized as particularly suitable, since it simplifies both receiving and
transmitting apparatus and also removes some sources of non-uniform transmission delay
between these components.
The construction of a composite signal containing these three individual signals requires
the synchronizing and picture signals to occupy different ranges of amplitude, since these
two classes of signals cannot be distinguished from one another by a frequency separation.
They must also occupy different time intervals. These requirements are satisfied by
assigning a range of potentials beyond black (and, therefore, called infra-black) to the
synchronizing signals and by inserting synchronizing signals in the time intervals provided
for scanning retrace. Figure 18 shows at 3 an oscillogram of two lines of a composite
signal showing line synchronizing pulses properly located in the retrace intervals. The
position of the leading edge of the pulse in the retrace interval is set a short time after the
beginning of the interval so that even receiver circuits of somewhat restricted band width
(and hence slow transient response) will have time to reach black level before the syn-
chronizing pulse begins, regardless of whether the picture edge is white or black. Failure
to provide this interval results in phase modulation of the scanning by the picture content.
This interval (sometimes called the "front porch") is made no greater than required by the
foregoing consideration, since any extra waiting at this point is at the expense of either
decreased time available for scanning retrace or decreased time available for picture.
The placement of the field signal conforms to the practice already described for the line
signal. The field signal is located in the same region of amplitude as the line signal and is
placed to occur during the vertical retrace region.
The portion of the transmission amplitude range not occupied by synchronizing signals
is reserved for the picture information.
THE RADIO-FBEQTJENCY SIGNAL
20-17
Picture-^] TL T
Hor. blanking— -1}*-
w Vertical
blanking 0.05 7°'03V
4— Bottom of ~
picture Tim-
I
« — -Top of picture
nftnnnni 1 1 1 1 1 i..i i n
Horizontal dimensions not to scaJe
Black
3 level
Detail
between
3<3 In 2.
White level-
Zero carrier
G) 0.004 H_»
max.
Detail
between
4-4 in 2.
Black level-*-
(Z)0.04 H— >
See note 6
<- (u) 0.004 H-*
max,
-v|L(&) 0.004 H
(p) 0.004 H.,
max.
~*
^(5)0.004 H
max.
^-Equalizing
pulse
Vertical
sync, pulse
f, 9/10 of
max. sync.
J, 1/10 of
iW)o.5Hij
f .,!-!, h
—jj-max. sync.
<Ar) 0.07 H± 0.01 H*
(s)0.004 H
(«)0,Q04 H
NOTE:
1. H= Time from start of one line to start of next line.
2. V —Time from start of one field to start of next field.
3. Leading and trailing edges or vertical blanking
should be complete In less than 0*1 H.
4. Leading and trailing slopes of horizontal blanking
must be steep enough to preserve mln. and max.
values of (as-fl/) and (£) under all conditions of
picture content*
*5. Dimensions marked with an asterisk Indicate that
tolerances given are permitted only for long time
variations, and not for successive cycles.
6. Equalizing pulse area shell be between 0.45 and
0.5 ot the area of a horizontal sync, pulse.
7. Refer to text for further explanations a.nd
tolerances.
FIG. 18. FCC Standard Television Synchronizing Wave Form
min.
9. THE RADIO-FREQUENCY SIGNAL
The composite signal of Fig. 18 may be applied to an r-f carrier as either amplitude,
phase, or frequency modulation. In television broadcasting, multipath transmission is
frequently observed; picture distortions caused by multipath transmission when phase or
frequency modulation is used are so serious that these methods of modulation have not
seemed practicable. Television broadcasting, therefore, makes use of amplitude modula-
tion.
20-18
TELEVISION
.2
£
O
O.
1
.i
"5
CD
THE K4DIO-FREQUENCY SIGNAL
20-19
POLARITY OF MODULATION. Polarity of modulation may be either positive (that
is, with an increase of image brightness represented by an increase of radiated signal) or
negative. Figure 19 illustrates these two forms, showing individual scanning line signals
for three distributions of picture content. A positive modulation polarity signal includes
at all times the synchronizing level (zero carrier) and the black level. It does not indicate
the level of peak white unless elements of this intensity are present in the picture. Neg-
ative modulation polarity, on the other hand, includes at all times the synchronizing level
(maximum carrier intensity), the black level, and peak white (zero carrier).
Automatic gain Control circuits for receivers require the presence in the received signal
of some characteristic which is independent of modulation. In sound transmissions, the
average value of the carrier has the required characteristic, but in television signals, the
average value is dependent on average picture brightness. White level, black level, or
synchronizing level must be used instead. Preferably, the peaks of the signal envelope
should be used, so that a simple peak detector may serve as the source of automatic gain
control information. It is found, therefore, that negative modulation polarity simplifies
very much the provision of automatic gain control in receivers.
The effects of impulse noise interference on signals of the two polarities are quite dif-
ferent. With positive modulation impulse noise usually produces bright spots in the re-
produced picture and has little effect on synchronizing signals. With negative modula-
tion impulse noise produces primarily black spots on the picture (which are on the whole
less disturbing than the bright spots produced with positive modulation) but has a greater
tendency to interfere with synchronizing signals. Since it is found possible to minimi&e
the effect of impulse noise on synchronizing sufficiently by careful circuit design in the re-
ceiver and since automatic gain control is believed desirable, American standards for tele-
vision have chosen negative modulation polarity.
BAND WIDTH. As was shown in article 3, the desired band width of television video
signals exceeds 4 megacycles. The application of this signal as amplitude modulation to
a carrier produces a signal having a total spectrum width which exceeds 8 megacycles.
Since radio channels are not available in unlimited quantities and since also the cost of
amplifiers is increased as their required band width increases, television broadcast practice
is based on vestigial sideband transmission. Curves A and B of Fig. 20 show the radio-
1.0
0.5
0.0
B
-5
-3-2-1 O I 2
Frequency Relative to Picture Carrier
01 23456
Frequency Relative to Assigned Channel Boundaries
FIG. 20 Radio-frequency Amplitude Characteristics. A. Double Side-band Transmission. B.
Vestigial Side-band Transmission Overall Characteristic. C. Vestigial Side-band Transmission;
Transmitter Only.
frequency amplitude characteristics for double sideband transmission and for vestigial
sideband transmission (references 19 to 24) .
The overall transmission characteristic for vestigial sideband transmission requires that
the signal originally produced with a carrier and symmetrical sidebands must be atten-
20-20 TELEVISION
uated selectively. The practice which has been standardized Is to provide a receiver
characteristic having the same form as the desired system overall characteristic. The
corresponding transmitter characteristic must, therefore, exhibit negligible attenuation
at all frequencies which are effectively transmitted by the receiver. It has therefore been
standardized as shown in Fig. 20 as curve C.
SOUND TRANSMISSION. The sound accompanying a television picture is trans-
mitted on a separate carrier whose frequency is located, with respect to the picture carrier
and its sidebands, as shown in Fig. 20. The sound carrier is frequency modulated with
maximum deviation of 25 kilocycles. The pre-emphasis practice standardized for fre-
quency-modulated sound broadcasting is also used for television sound.
FREQUENCY ALLOCATION. Because of the wide frequency channels required for
television, allocation of channels below 50 megacycles would interfere with so many exist-
ing services as to be impracticable. Television allocations for commercial use, therefore,
lie in the range between 54 and 216 megacycles, as shown in the table. Allocations at
higher frequencies have been made for experimental and relay use.
NOMINAL PICTUEB SOUND
CHANNEL BOUNDARIES CARRIER CARRIER
2 54- 60 55.25 59.75
3 60- 66 61.25 65.75
4 66- 72 67.25 71.75
5 76- 82 77.25 81.75
6 82- 88 83.25 87.75
7 174-180 175.25 179.75
8 180-186 181.25 185.75
9 186-192 187.25 191.75
10 192-198 193.25 197.75
11 198-204 199.25 203.75
12 204-210 205.25 209.75
13 210-216 211.25 215.75
POLARIZATION OF RADIATED SIGNAL. A simple horizontally polarized dipole
antenna has a horizontal directive pattern which is sometimes useful in minimizing ef-
fects- of multiple transmission paths. Since in other respects there is little net advantage
either way between horizontal and vertical polarization, horizontal polarization has been
standardized.
10. STANDARDS
The Federal Communications Commission has established the following Standards of
Good Engineering Practice for television broadcasting:
1. The width of the television broadcast channel shall be 6 megacycles per second.
2. The visual carrier shall be located 4.5 megacycles lower in frequency than the aural center fre-
quency.
3. The aural center frequency shall be located 0.25 megacycle lower than the upper frequency limit
of the channel.
4. The visual transmission amplitude characteristic shall be as shown in Appendix II [curve C of
Fig. 20].
5. The number of scanning lines per frame period shall be 525, interlaced 2:1.
6. The frame frequency shall be 30 per second, and the field frequency shall be 60 per second.
7. The aspect ratio of the transmitted television picture shall be 4 units horizontally to 3 units verti-
cally.
8. During active scanning intervals, the scene shall be scanned from left to right horizontally and from
top to bottom vertically, at uniform velocities.
9. A carrier shall be modulated within a single television channel for both picture and synchronizing
signals, the two signals comprising different modulation ranges in amplitude (see Appendices I and II)
[Figs. 18 and 20].
10. A decrease in initial light intensity shall cause an increase in radiated power (negative trans-
mission).
11. The black level shall be represented by a definite carrier level, independent of light and shade in
the picture.
12. The pedestal level (normal black level) shall be transmitted at 75 per cent (with a tolerance of
plus or mintis 2.5 per cent) of the peak carrier amplitude.
13. The maximum white level shall be 15 per cent or less of the peak carrier amplitude.
14. The signals radiated shall have horizontal polarization.
15* A radiated power of the aural transmitter not less than 50 per cent or more than 150 per cent of
the peak radiated power of the video transmitter shall be employed.
LENS APERTURE REQUIRED 20-21
^ 16.* Variation of Output. The peak-to-peate variation of transmitter output within one frame of
video signal due to all causes, including hum, noise, and low-frequency response, measured at both
synchronizing peak and pedestal level, shall not exceed 5 per cent of the average synchronizing peak
signal amplitude.
17.* Black Level. ^ The black level should be made as nearly equal to the pedestal level as the state
of the art will permit. If they are made essentially equal, satisfactory operation -will result and im-
proved techniques will later lead to the establishmejxb of the tolerance if necessary,
18.* Brightness Characteristics. The transmitter output shall vary in substantially inverse loga-
rithmic relation to the brightness of the subject. No tolerances are set at this time,
See also reference 28 for an extended discussion of standards.
TELEVISION BROADCASTING
By T. J. Buzalski, A- I,, Hammcrschjnidt, apd F, J. Somers
A modern television broadcasting plant provides facilities for the pick-up and broad-
cast of entertainment, news, and cultural and educational subject matter in both sight
and sound. The purpose of such a plant is to provide an adequate and satisfactory public
service, and this requires a flexible and well-coordinated installation. A functional sub-
division of equipment and facilities is the following:
(a) Studio and control facilities (picture and sound) .
(6) Field pick-up and relay facilities (picture and sound).
(c) Visual and aural broadcast transmitters.
Typical studio and control facilities consist of one or more live-talent studios, a film
pick-up studio, a video effects studio, one or more announcers' booths, and a master con-
trol room having switching and monitoring facilities for feeding the various studio outputs
or remote pick-up outputs to the transmitter, as required. The master timing or syn-
chronizing generator, various picture Hue amplifiers, power supply rectifiers, and other
equipment common to the studio facilities system are usually grouped in a main equip-
ment room for maximum efficiency and ease of maintenance.
Field pick-up facilities include portable television cameras with their associated control,
monitoring, and synchronizing equipment and portable sound equipment. Either radio
relay circuits, coaxial cables, or equalized telephone lines are used to transmit the picture
signals back to the master control room of the broadcast station proper. The sound por-
tion of the program is generally transmitted back by wire line, though radio circuits are
used where wire facilities are not available. Field pick-ups also encompass the use of
mobile equipment where the television cameras, along with their synchronizing, control,
and monitoring equipment, are mounted in a moving boat, aircraft, or other means of
locomotion.
The need for maximum height of the transmitting antenna to provide line-of-sight re-
ception for as many receivers as possible usually requires that the visual and aural trans-
mitters be located remote from the television studios. The visual lirik between the master
control switching point and the transmitter may be a radio relay circuit, a coaxial cable,
or an equalized telephone line. The aural link between the master control point and the
transmitter is usually a wire line.
In order to coordinate operations and to assure program continuity, the television plant
must be provided with an adequate and flexible intercommunication and order wire sys-
tem separate and apart from the sound program pick-up, control, and transmission equip-
ment.
1L LENS APERTURE REQUIRED
The lens speed required for a given camera pick-up tube and scene illumination is best
determined by experiment under operating conditions or from data supplied by the tube
manufacturer. If it is desired to compute the lens speed which will provide a sufficiently
bright image to meet the requirements of a given pick-up tube, the following formulas
{see reference 33) are applicable:
F (focal length of lens) = — cot ^ inches (1)
aperture)
* These items are subject to change but are considered.the best practice under the present s*ate of
the art. They will not be enforced pending a further determination thereof.
20-22
TELEVISION
where W = the width in inches of the pick-up tube sensitive surface.
a = the desired horizontal angle of view in degrees,
s = the pick-up tube sensitivity in signal microamperes per lumen.
B — the surface brightness of the scene in candles per square foot.
T — the light transmission factor of the lens (usually between 40 and 60 per cent) .
N — the required peak picture signal-to-rms noise ratio.
7n = the equivalent rms noise current (amperes) at the input of the amplifier used
with the pick-up tube.
The noise generated in pick-up tubes without electron multipliers is small compared
with that originating in the first tube of the video-preamplifier. Noise currents generated
in the first video amplifier stage result from two significant components : thermal agitation
noise in the input circuit and current fluctuations in the plate circuit of the first video
amplifier tube. An expression combining these components for the computation of the
equivalent rms noise current ( Jn) follows (see reference 33) :
^ (3)
where In = equivalent rms noise current in amperes.
k = Boltzmann constant (1.37 X 10~23 joule per °K).
T « absolute temperature (300° K).
fm — pass band of amplifier in cycles per second.
R — input resistor of amplifier in ohms.
Rt = equivalent grid resistance of input tube for noise in ohms at 300° K (for first
video amplifier tube).
C — total shunt capacity (pick-up tube, stray capacity, and video amplifier in-
put capacity).
In a non-storage pick-up tube where the photoelectrons are amplified by an electron
multiplier incorporated in the pick-up tube, the predominant noise originates at the
photo cathode. (See reference 34.) The equivalent rms noise cm-rent in this case is given
by the following expression:
In — ^/2eiofm amperes (4)
where io = current for one picture element.
e - electron charge = 1.59 X 10~19 coulomb.
fm — pass band of equipment (cycles per second) .
It should be pointed out that the sensitivity s of a pick-up tube in signal microamperes
per lumen is not necessarily a constant. In some types of tubes « is a function of the in-
cident light. This is illustrated by the curve of Fig. 1, which shows s for a sample Icono-
.150
£.125
•5.010
o.075
&.050
CO
.025
0 J. .2 .3 .4 .5 6 .7 .8 .9 ,10
Light on mosaic, lumens
FIG. 1. Signal Output vs Illumination Characteristic of a Typical Iconoscope
scope (reference 56). Another type of tube having a non-linear sensitivity curve is the
Image Orthicon (reference 30) . The signal output vs. illumination curves of the Orthicon
and the Image Dissector are essentially straight lines.
12. STUDIO CAMERA DESIGN
Aside from the pick-up lens, view finder (references 31 and 32), and other optical re-
quirements, the electrical and mechanical design of the studio camera must be given care-
ful consideration. Experience has shown that the following principles should be followed
in the design:
STUDIO CAMERA DESIGN 20-23
(a) In order to keep the camera as small, light, and mobile as possible, the number of
tubes and components housed in the camera proper should be kept to the mim'rnttm. As
much auxiliary equipment as possible should be mounted on permanent racks in or near
the control room.
(&) All electrical camera controls and adjustments which may require attention during
a broadcast should be located at or within easy reach of the control-room console.
(c) The mechanical layout of the camera should facilitate rapid servicing in case of
failure. Such features as replaceable plug-in type video preamplifiers will simplify main-
tenance of the camera.
A variety of different types of camera tubes have been used for television studio pick-up.
Before 1946 the Iconoscope camera found the widest acceptance among television broad-
casters. Subsequently the Image Orthicon (reference 30) with its greater light sensitivity
has been found to have practical advantages for studio use. Since space does not permit
a detailed discussion of all camera types, the Iconscope has been chosen in the following
example since it embodies many features that are common to present television cameras.
In a typical Iconoscope studio camera design, the following items are included in the
camera housing proper:
(a) Video preamplifier (five tubes) including a high-peaker stage and a cathode follower
to feed a 75-ohm coaxial line.
(6) Beam blanking amplifier (double triode).
(c) Horizontal and vertical deflection coils in a yoke assembly arranged to be fed from
an external source via coaxial cables.
(d) Bias lighting arrangement for improving the collection of secondary electrons from
the mosaic.
(e) Filament transformer (110-volt alternating current to 6.3-volt alternating current
60 cycles).
This particular design of camera used an optical view finder and was mounted on a
movable pedestal equipped with a pushbutton-controlled motor-driven elevating arrange-
ment, a suitable tilting and panning head being provided for mounting the camera.
A typical flexible cable for connecting the camera to the rack equipment has conductors
and insulation as shown in Table 1. As indicated in the table, this cable has been designed
as an all-purpose cable which can be used with a variety of camera and pick-up tube types.
Conductors 26 and 27 are coaxial cables, conductor group 28, 29 is a shielded balanced
twisted pair video cable. Conductors 3 and 4 are used to feed high voltage to the pick-up
tube. Video cable shields should be run separately from the common power supply cir-
cuit ground to avoid possible interference pick-up due to common ground return imped-
ance.
i For camera cable lengths of 100 to 150 ft maximum, it is practical to locate the deflection
wave generators in the control-room racks, provided sufficiently low-impedance deflection
coils are used in the camera -deflection yoke. For longer cable lengths, it is advisable to
locate the deflection amplifiers in the camera proper or in the camera pedestal, feeding the
horizontal and vertical driving pulses or sawtooth waves out to the camera from the racks
via terminated 75-ohm coaxial cables or terminated balanced pair twinax cables.
Some types of camera tubes are easily damaged if the deflection circuits fail during
operation. This is true of Iconoscopes. Orthicons may also be damaged if the mosaic is
illuminated when the deflection failure occurs. It is, therefore, necessary to provide pro-
tective devices to bias off the scanning beam automatically when deflection fails. Relays
actuated by rectified deflection currents have proved satisfactory for this purpose.
The video output of the camera may be fed to the control room from the camera either
by a coaxial line or by a balanced twisted pair transmission line with an external grounded
shield. The latter is preferred to give better discrimination against hum pick-up in long
cables.
The camera preamplifier design usually provides for a peak-to-peak video output from
the camera of between 0.1 and 1.0 volt. The higher levels are preferred to provide dis-
crimination against possible interference pick-up in the cable.
VIDEO PREAMPLIFIER DESIGN. The scene brightness, the speed of the lens, the
sensitivity of the pick-up tube, and the value of pick-up tube signal load resistor being
known, the low-frequency gain required of the preamplifier to bring the signal up to the
desired level to feed the 75-ohm cable can readily be calculated. (By low-frequency gain
is meant the gain for video frequencies below 50 or 100 kc.) The high-frequency gain re-
quired of the amplifier, assuming that the general practice of feeding a "flat" signal to the
line is followed, is dependent on the frequency and phase distortion introduced at the in-
put of the preamplifier by the network used to couple the output of the pick-up tube to the
grid of the first stage of the preamplifier. Use of a high value of load resistor (30,000 to
100,000 ohms) compared to the value which would be chosen for flat response (1000 to
Table 1. Flexible Cable Used between Television Cameras and Equipment Racks
Conductor
Cable Mfrs. Maximum
A.W.G.
No.
Function
No.
Color
E
(AC)
E
(DC)
I
(Amps)
Orthicon
Iconoscope
Image Orthicon
I
White
250
450
2.4
20
Mult, focus +150
volts to +250 volts
Ike focus —350 volts
to -600 volts
Mult, focus +T50
volts to +250 volts
2
3
Bkck
Ring —50 volts to
+150 volts
Decelerator —50 volts
to +150 volts
Yellow
1000
1400
Ike grid —950 volts
to —1150 volts
Image focus 200 volts
to —1000 volts
4
_
Red
2000
2800
Multiplier +1000
volts to +2000 volts
Ike cathode -1000
volts to —1200 volts
Multiplier +1000
volts to +2000 volts
Black
4.0
18
1 10 volts a.c.
110 volts a.c.
110 volts a.c.
6
7
White
Red
250
450
2.4
20
Bias -105 volts
Bias —105 volts
Bias —105 volts
8
Brown
Video +51 +280 volts
Video +B +280 volts
Video +5 +280 volts
9
Orange
Deflection + B
Deflection + B
TO
White
50
70
Horizontal center
Edge light
Horiz. center
11
Black
Back light
12
Red
Target —15 volts to
+15 volts
Target —15 volts to
+15 volts
13
Green.
250
450
Beam 0 to —45 volts
Beam 0 to —45 volts
14
_
Black
Signal light
Signal light
, Signal light
Vertical deflection
Vertical deflection
Vertical deflection
16
Red
17
White
Program phone
Program phone
Program phona
18
Red
19
Blue
Wall focus +100 volts
to +250 volts
Wall focus +100 volts
to +250 volts
20
Green
50
70
Alignment field
Alignment field
21
Black
250
450
Phone
Phone
Phone
22
Green
23
24
White
Front focus field
Front focus field
Yellow
25
Blue
50
70
26
27
Brown
600
850
Horizontal S.T.
Horn, deflect.
Horiz. driving
Orange
Blanking
Blanking
Blanking
28
; Yellow
300
500
Video
Video
Video
29
Blue
30
Yellow
50
70
Rear focus field
Rear focus field
31
Brown
32
Orange
Alignment field
Alignment field
20-24
STUDIO CAMERA DESIGN
20-25
3000 ohms) offers advantages in discrimination against low-frequency noise and micro-
phonic disturbances in the first preamplifier stage, because it results in a relatively greater
level of low-frequency signal being applied to the first grid than if a flat system is used.
On the other hand, tubes having a self-contained electron signal multiplier such as the
Image Dissector or the Image Orthicon can provide a relatively large signal output current
so that a relatively low value of signal load resistor can deliver sufficient signal voltage, m
many cases, to override noise and microphonic disturbances generated in the first therm-
ionic amplifier stage.
"When a high value of signal load resistor is used, it is the practice to compensate for the
frequency and phase distortion introduced by incorporating a "high-peaker" stage in the
video preamplifier. Figure 2 is a block diagram illustrating one form of high-peaking.
Pickup tube
(EZ»
Load resfstor-
6-i-~ £ +
FIG. 2. High Peaker Stage Employing Resistance and Inductance in the Plate Circuit
The load impedance Z\ for the pick-up tube consists of Ri and Ci in parallel, d being the
combined output capacitance of the pick-up tube, stray and wiring capacitances, and the
input capacitance of the first video amplifier stage. The video amplifier stages following
the input circuit are designed for uniform response over the required band width. These
feed a high-peaker stage Vi having an effective plate load impedance Z% at high frequencies
consisting of R% and Z/2 in series (neglecting £2) . Since the internal impedance of both the
pick-up tube and Vi will be relatively high (they may be considered as constant-current
generators) and since the amplifier between the pick-up tube and V\ is designed for uni-
form response, the overall response of the system is proportional to the product ZiZ%. If
the values of Z\ and Zz are chosen so that ZiZ% = A? = constant (inverse networks) , an
Normal Interstage
7 shunt peaking
i
100,000
82
i
£ 10-110
:
/
5
| Normal low-f
I— ,&? compens*
= 2 MF
6800 =;
•=• High-peaking
adjustment
(.280 v O
«
•
<
<
•
f
Fia. 3. High Peaker Stage Utilizing Variable Cathode By-pass
overall flat response will be obtained for frequencies below the point where the resonance
of Ca with 1/2 begins to have important effect. This condition is fulfilled when R^C\ =
LZ/RZ. It has been found that, if Z/2 is chosen such that the resonance of Ca with L% occurs
at a frequency about 1.5 or more times higher than the top video frequency for which the
balance of the amplifier is designed, the effect of C2 can be neglected.
Obviously, by adding a series coil to the input circuit, a pair of inverse networks could
be provided which would exactly compensate for the distortion including the effect of Cj.
20-26
TELEVISION
From a practical standpoint, however, the simpler arrangement of Fig. 2 has been found
to give satisfactory results. Two other high-peaker circuits which are simple and yet can
be designed to give satisfactory compensation over a reasonably wide band are illustrated
in Figs. 3 and 4. A variety of other circuits and compensation methods can also be used.
The low-frequency compensation of the preamplifier generally follows standard practice,
the amplifier being designed to pass without appreciable distortion a 60-cycle square wave
applied to the input terminals. In some designs of Iconoscope preamplifiers, an additional
network consisting of 150,000 to 300,000 ohms shunted by 0.001 to 0.005 pi is placed in
series with the low-potential end of the signal load resistor to obtain improved operation
6AC7
3900
+ 280 v O-
FIG. 4. High Peakcr with Variable Series Capacitor
at low and medium frequencies. When this is done, an appropriate network must be in-
serted in one of the later stages of the amplifying system to compensate for this low-
frequency pre-emphasis.
13. STUDIO EQUIPMENT
CONTROL ROOM. In a typical studio control room for Iconoscope cameras, the
rack equipment for each camera chain consists of the following:
(a) Horizontal deflection sawtooth wave generator, with the output modulated by
sawtooth waves of vertical frequency for keystoning. The amplitude of the sawtooth
wave, as well as the amount of keystoning, is adjustable. An output transformer feeds
the low-impedance deflection coils in the camera via a 75-ohm coaxial cable. An im-
pedance step-up transformer located in the camera is sometimes used to feed the de-
flection coils.
(Z>) Vertical deflection sawtooth wave generator with an output transformer feeding a
75-ohm coaxial line which connects to the camera vertical deflection coils. An impedance
step-up transformer located in the camera is sometimes used to feed the deflection coils.
(c) Regulated power supplies for deflection amplifiers, video amplifiers, and the Icono-
scope.
(d) Studio amplifier. This amplifier provides video Outputs for feeding monitoring
circuits and the master control room. The output circuits feed 75-ohrn coaxial lines at a
signal voltage level between 0.5 volt and 1.0 volt peak to peak, depending on the standard
level adopted for a given plant. The output of the studio amplifier contains picture
blanking signals but not synchronizing signals. An excess of picture blanking signals is
introduced in one of the later stages of the studio amplifier followed by an adjustable
clipper or pedestal (brightness) control. The amplifier is provided with a video gain con-
trol.
(e) Shading amplifier. Certain types of camera tubes, including the Iconoscope, gen-
erate a spurious signal output in addition to the signals representative of picture informa-
tion. The effect on the television picture of uncompensated spurious signals is to produce
shaded areas not present in the original scene.
STUDIO EQUIPMENT 20-27
It has been found in practice that the effect of spurious signals can readily be compen-
sated by the addition of a few simple wave forms of appropriate amplitude and polarity to
the camera video output. Since the shading wave forms and amplitudes required vary
with scene illumination, it is the practice to provide individual manual adjustment of
shading waveforms for each Iconoscope camera. Pick-up tubes which do not always re-
quire shading signals are the Image Dissector, the RCA type 1840 Orthicon, and the
Image Orthicen.
The following shading wave forms, adjustable in amplitude and polarity, are provided
for each camera chain: (1) horizontal sawtooth; (2) vertical sawtooth; (3) horizontal
parabola (adjustable clipping); (4) vertical parabola (adjustable clipping); (5) vertical
sine wave with adjustable phase (the inclusion of vertical sine wave is optional).
When a studio is equipped with more than one Iconoscope camera, it is usually econom-
ical to provide a shading generator having a low-impedance pushpull output bus for each
shading wave form. Relatively high-impedance center-tapped potentiometers can then
be connected in parallel with these buses to feed a shading isolation and mixing amplifier,
associated with each camera chain.
Shading signals should be added to the video signal in a low-level stage of the video sys-
tem prior to the introduction of picture blanking. Introduction of shading into a low-
level stage (it is sometimes fed into an early stage of the preamplifier in the camera) tends
to prevent overload of the higher-level stages due to uncompenaated tilt in the video signal
wave form.
The following operating controls should be located on the studio console for each camera
chain: (1) Iconoscope beam current; (2) Iconoscope focus; (3) video gain (contrast); (4)
pedestal (brightness) ; (5) all shading controls.
The following controls which generally require attention only during initial warm-up
of the equipment need not be mounted on the console but should be within easy reach of
the video operator: (1) vertical deflection amplitude; (2) vertical deflection centering;
(3) keystone adjustment; (4) horizontal deflection amplitude; (5) horizontal deflection
centering; (6) bias light adjustment.
Though the example given above deals with Iconoscope cameras, the same general
principles and layout apply for other types of pick-up tubes, except, of course, that dif-
ferent arrangements of operating controls and adjustments are necessary. The need for
shading signals is generally associated with Iconoscopes alone, but availability of at least
sawtooth and parabola wave forms is often advantageous when using other types of camera
tubes which nominally do not require it. Thus a tube with somewhat non-uniform sen-
sitivity over different parts of its photoelement may produce a satisfactory picture if
shading signals are available.
AMPLIFIER DESIGN. In the usual equipment layout, the studio amplifier performs
the following functions:
1. Provides for the insertion of shading wave forms if they have not previously been
added in the preamplifier.
2. Provides for the addition of picture blanking signals of adjustable amplitude to the
video signal.
3. Provides for variable gain control (automatic gain control is sometimes used) of the
video signal.
4. May include one or more of the following corrective features: (a) gamma correction;
(b) aperture distortion correction; (c) correction for phase distortion.
5. The studio amplifier usually provides at least two independent outputs of combined
video and blanking signals at levels of 0.5 volt to 1.0 volt peak to peak at 75-ohm im-
pedance. One of these outputs normally feeds the master control and switching point
where the studio output may be switched to the transmitter. The other output feeds the
local studio picture monitoring circuits.
The video coupling networks used in the studio amplifier follow the conventional de-
signs. Shading signals are generally added via a tube whose plate or cathode feeds an
impedance common to a plate or cathode of one of the video stages. Blanking signals
are generally added through a tube whose plate feeds an impedance common to the plate
of one of the later video amplifying stages. An excess of picture blanking signal is added,
being clipped off by a variable clipping arrangement in the following video stage. Care
should be exercised in the design to provide an exceptionally linear clipping arrangement
to avoid crowding of signal voltages corresponding to the darker portions of the picture.
MONITORING AND SWITCHING FACILITIES. Studio monitoring facilities gen-
erally consist of a picture monitor showing the outgoing picture plus one picture preview
monitor for each camera in operation in the studio. The outgoing picture or "on the air"
monitor should preferably be fed through a return feed from the master control point and
should be synchronized from the synchronizing signals which have been added to the video
20-28
TELEVISION
and blanking components at the master control point. The preview monitors are gen-
erally of the "driven type," i.e., locked-in by the horizontal and vertical driving pulses
utilized to operate the camera deflection circuits. When this is done, the preview monitors
may be switched from one camera output to another without loss of synchronization.
Also, since the camera outputs normally do not provide synchronizing signals, the use of
driving impulses gives more stable results than blanking signals for preview monitor
synchronization. The on-the-air monitor should be synchronized from pulses contained
in the composite input signal, however, because it is often necessary to connect it to view
pictures supplied from other sources in the normal course of operations.
One satisfactory method of switching the video monitors is to provide them with high-
impedance inputs (via cathode followers in some designs) so that one or more can be
switched to the 75-ohm monitoring output bus of any one of the studio amplifiers. Mon-
itor switching may be accomplished by mechanical switches, by switching relays, or by
electronic means. A relay switching system controlled by a set of pushbuttons and in-
dicator lamps mounted on the control console is sometimes used.
In addition to picture monitoring facilities, wave-form monitors have to be provided
as a continuous check on the shading and voltage level of the signal generated by each cam-
era chain as well as that being fed out of the studio. A pushbutton-controlled switching
system for the wave-form monitors is desirable.
TIME DELAY NETWORKS. In the usual television studio plant having more than
one studio or signal source, it is the practice to add the synchronizing signals to the video
R— "sir
0<1^8R =s self-lad ucta nee of each coll.
M= -—: — s mutual Inductance of LI and La. ( Colls are wound so- that the fields are series aiding, thus gfvFnff an
effective negative mutual Inductance).
/—top frequency required to reproduce original pulse.
R = deslgn Impedance.
Approximate delay per section —"^ — seconds.
The LI, L2. M assembly Is a single-layer coil with a center tap, the wire size spacing between turns and diameter
of form being so chosen that the following conditions are satisfied.
A center tapped coll satisfying these conditions Is the
equivalent of two colls each of seff-Inductance Li and
of negative mutual inductance M
, U-M
—
FIG. 5. Delay Network Employing Negative Mutual Inductance
and blanking signals at one point in the system, usually the master switching or control
point. This is done for the following reasons: (1) failure of the studio output does not
disturb the transmitter or throw receivers out of synchronization; (2) synchronizing signal
level fed to the transmitter can be made independent of variations in studio output level;
(3) insertion of synchronizing signals in the system at a single point just prior to the studio-
transmitter link is the most practical way to maintain synchronizing signals at the exact
level required by the transmitter.
Since the cables connecting the various studios with the master control position are
usually of different lengths, electrical networks are employed to delay the signals arriving
via shorter cables so that the proper "front porch" margin between the starting time of the
horizontal picture blanking pulses and the starting time of the horizontal synchronizing
pulses will be maintained when synchronizing signals are added. The delay networks
usually consist of a number of sections of artificial line utilizing lumped constants. Though
it would be possible to insert the delay networks in the studio video outputs, it is gen-
GAMMA (TRANSFER CHARACTERISTIC) 20-29
erally preferable to insert them in the coaxial lines feeding the studio with the camera driv-
ing, camera blanking, and picture blanking signals. This is more economical as less perfect
delay networks can be used and the effects of any slight transmission line reflections due
to incorrect termination can readily be removed by clipper stages in the studio deflection
and blanking amplifiers.
DESIGN OF DELAY NETWORKS. Studio delay networks may be designed in a
number of forms. ^ A common type is an artificial line with Z0 = 75 ohms in the form of a
ladder network with a number of series coils and shunt capacitors. This type of artificial
line may be treated as a low-pass filter with the cut-off chosen somewhat higher than the
top operating frequency. As in usual filter practice, this type of network is best ter-
minated by a double M-derived network at its output. A design using negative mutual
inductance which gives excellent performance is shown in Fig. 5. The top operating fre-
quency may be chosen on the basis of the number of harmonics of line-scanning frequency
required to reproduce a pulse of a given steepness. The order n of the highest harmonic
required is n = lOO/p, where p is the time of rise of the wave expressed in percentage of
the fundamental period (reference 35) .
Continuous lengths of transmission line can be used in lieu of lumped delay networks.
If a continuous length of line is used for time delay, it should have reasonably low attenua-
tion and uniform time delay over the required frequency band.
14. GAMMA (TRANSFER CHARACTERISTIC)
The term gamma (7), has been used to define the slope of the curve of the logarithm of
image brightness vs. the logarithm of object brightness (reference 36). Unless otherwise
specified, the slope 7 refers to the central linear portion of the curve, between the ex-
tremities of the brightness values considered.
Though the term gamma is a useful concept when making comparisons with photog-
raphy, the trend is away from it in connection with television systems. As a matter of
fact, the term must be applied with caution since it often leads to erroneous conclusions.
The reason for this is twofold. First, gamma, being a numeric and referring only to the
central portion of the characteristic, tells nothing about the effect of the shape of the toe
and knee of the curve; second, the concept is difficult to apply in many portions of the
television system where a reference to picture black is not directly available. Therefore,
the term gamma, if used at all, should be restricted to comparisons of original scene bright-
nesses and final image brightnesses in an overall sense.
"Transfer characteristic' '„ (reference 28) is the name that has been given to the logarith-
mic plot of light input vs. signal voltage output of a television transducer. Thus, the
Iconoscope performance curve of Fig. 1, plotted to logarithmic coordinates, could be called
the "signal current vs. illumination transfer characteristic" of an Iconoscope.
GAMMA CORRECTION. It can be shown that the overall signal-to-noise ratio of a
television pick-up, transmitting, and receiving system is improved by transmitting a
logarithmic light vs. voltage characteristic. Though the exact shape of the curve has not
been, standardized (1949), it appears to be accepted that the light vs voltage character-
istic of the Iconoscope (see Fag. 1) is close to the ideal shape. The reproducer normally
has the opposite curvature to Fig. 1. This is conveniently obtained by providing a picture
tube with the required light output vs. grid voltage transfer characteristic.
When a pick-up tube such as an Image Dissector or an RCA type 1840 Orthicon, having
linear voltage output vs. illumination transfer characteristic, is used, it is necessary to
incorporate a non-linear element in the amplifying system to achieve the desired logarith-
mic curvature. An amplifier designed for this purpose is called a gam ma-correction
amplifier.
A wide variety of circuits may be used for gamma correction. The following design
principles apply: (a) Black level must be established at the input to correction stage so
that the correction can be applied independent of the excursions of the AC axis of the video
signal with respect to black level. (6) The correction should be applied prior to the video
stage in which picture blanking pedestals are inserted, (c) The correction amplifier should
be designed so that the amount of correction applied is variable between no correction at
all and the maximum value. The maximum value is limited by the minimum signal-to-
noise ratio that can be tolerated. A difference in video gain between the signals corre-
sponding to the dark portions and the light portions of the picture of 10 : 1 or even 100 : 1
is often desirable. A gain difference of 10 times is the most that can be used in many
cases, however, owing to signal-to-noise ratio limitations. The amount of correction to
be applied for a given soene is subject to artistic as well as technical requirements, (d)
For a television, system capable of reproducing only a relatively narrow contrast range, the-
20-30
TELEVISION
exact shape of the gamma-correction curve is relatively unimportant as far as the eye is
concerned when viewing the overall result.
A common type of gamma-correction amplifier utilizing tubes of different character-
istics in parallel is shown in Fig. 6. Another system having a diode connected across the
cathode resistor of a video stage is shown in Fig. 7.
.6 v to 10 v
peak to peak
6AC7 50
Video output
IRj
>— Black level
_rfffftf\_|| —
~~
7 adjustment changing
screen voltage from
+25 v to +150 v
FIG. 6. Gamma Correction Stage Using Tubes in Parallel
White,
— 105 v
Note: Ri controls change In '
R2 controls signal level
at which change In 7
occurs
R3 controls black-level clipping
at Input
FIG. 7. Gamma Correction Stage with Variable Cathode Degeneration
15. APERTURE CORRECTION
When the size of the pick-up or reproducer scanning spot is appreciable compared to a
picture element, aperture distortion takes place. For a mechanical scanning system or
an equivalent system in which the dimensions of the scanning spot are accurately known,
the amplitude vs. frequency distortion caused by the finite size of the aperture may be
FILM PICK-UP 20-31
accurately calculated (reference 6). For cathode-ray systems the effects of aperture dis-
tortion are best determined by test. In a pick-up tube using cathode-ray beam scanning,
for example, the effects of aperture distortion may be measured by determining the signal
output obtained by scanning different patterns of uniformly illuminated alternate black
and white lines of various pitches. A measured signal output vs. picture element size
curve having been obtained for a given type pick-up tube, an amplitude correction equal-
izing network may be designed to compensate for the aperture distortion (reference 2).
The complete aperture correction equalizer should include a phase equalizer to compensate
for any phase distortion introduced by the amplitude correction network. Apertures of
irregular shape may also introduce phase distortion. The aperture correction network,
if designed for a characteristic impedance of 75 ohms, may be connected between the studio
amplifier output and the coaxial line feeding the master control position.
The amount of aperture correction that can be applied in a given case is limited by the
extent to which a corresponding reduction in the signal-to-noise ratio of the studio output
can be tolerated. As a practical matter, it is found that the inherent resolution capa-
bilities of most types of television pick-up tubes is great enough so that a special network
for aperture correction is unnecessary. Adjustment of the high-peaker stage (see article
12) for the sharpest picture may often include some inadvertent correction for aperture-
distortion effects.
16. FILM PICK-UP
To assure program continuity and flexibility the following may be considered the min-
imum equipment requirements for the television film pick-up studio: (1) two television
film pick-up cameras with associated control, monitoring, and amplifying equipment; (2)
two 35-mm sound-mo tion-picture projectors; (3) two 16-mm sound-motion-picture pro-
jectors; (4) two 35-mm slide projectors; (5) sound control and monitoring facilities.
The amplifying, control, and monitoring equipment for the film pick-up studio is es-
sentially the same as that for the direct pick-up studio. Additional console controls re-
quired are remote projector starting and phasing. Since the synchronizing generator is
generally locked-in with the local power mains, synchronous motors are used to operate the
film projectors. A convenient method of phasing the projectors is to shift the phase of the
synchronizing-generator 60-cycle reference voltage, thereby shifting the phase of camera
scanning with respect to the projector. Mechanical phasing methods are also satisfactory.
Both storage and non-storage types of pick-up tubes are suitable for television film
pick-up. Since the standard sound film frame rate is 24 per second and the standard tele-
vision frame rate is 30 per second, the difference is made up by scanning consecutive
frames 2 and 3 times respectively at the 60-cycle interlaced field deflection rate.
In the case of non-storage-type pick-up tubes, such as the Image Dissector, the optical
image of the film or an appropriate section of it must be projected optically on the photo-
cathode at the time scanning takes place. Intermittent film projection is not considered
practical for non-storage tubes since the film pull-down time is limited to approximately
0.00117 second according to present standards. Special projection methods are therefore
required. Some of these employ uniform motion of the film in conjunction with optical
and electronic means to provide scanning of alternate film, frames in the required 2,3
sequence (reference 37).
For storage-type pick-up tubes, such as the Iconoscope, the optical image is flashed on
the mosaic during vertical blanking time and the stored "charge-image" scanned off dur-
ing the normal vertical scanning time (reference 38) . The film is moved during the ver-
tical scanning time when the mosaic is dark. For 35-mm film a special intermittent mo-
tion designed so that the interval between pull-downs alternates between 1/20 and 1/30
second may be used to attain the required projection sequence, the maximum film pull-
down time available being approximately 0.015 second under 1946 standards. Projectors
for 16-mm film can be designed for a pull-down time of 0.007 second or less, in which case
a normal equally spaced intermittent may be used. A synchronously driven rotating
shutter placed between the projector lens and the pick-up tube is used to flash the picture
on the mosaic. Proper phasing between the light flashes and the scanning may be obtained
by mechanical or electrical means.
Automatic brightness control (automatic adjustment of the picture blanking clipper
bias in the studio amplifier) may be provided for film pick-up by means of an auxiliary
photocell to pick up the light from the film a few frames ahead of projection. This photo-
cell output is integrated and applied to the blanking clipper bias circuit.
20-32
TELEVISION
17. MASTER CONTROL POSITION
In the usual television plant, where there are several signal sources, including remote
pick-ups, all switching and the final monitoring of the signal before it is sent to the trans-
mitter are done at a central point called the master control position. The synchronizing
generator, the synchronizing signal distribution amplifiers, the video line amplifiers, and
the various items of test equipment used in connection with operations are usually located
in a main equipment room adjacent to the master control position.
A typical studio master control pulse and video system layout is shown in Fig. 8. The
synchronizing generator outputs are fed to the inputs of a number of pulse distribution
I DIRECT PICK-UP STUDIO
CAMERA
DIRECT STUDIO CAMERA RELAYS
PUSHBUTTON CONTROLS IN
STUDIO CONTROL CON-SOLE
Main equipment room
VIDEO LINE
FIG. 8. Block Diagram Showing Pulse Distribution to Studios and Video Switching Circuits at the
Master Control Position
amplifiers as shown. A separate pulse distribution amplifier feeds each studio and the
monoscope. A separate distribution amplifier is also reserved for synchronizing signals.
This system of pulse distribution isolates one studio from another so that an accidental
short circuit or failure in a pulse line to one studio cannot affect the others. A spare pulse
distribution amplifier is held in readiness in case of failure of one of the amplifiers. It is
also good practice to have a spare synchronizing generator in operation at all times and to
provide means for quickly switching it into service if the regular generator fails.
As shown in the diagram, delay networks are inserted in the pulse lines to all studios
except the one having the longest cable run. The delay networks are adjusted (by adding
or removing sections) so that the time of arrival of the blanking signals from each studio
at the master control position switching relays will be the same and will be such that the
proper front porch delay of synchronizing signals will be maintained when the signals are
added. There is generally enough coincidental time delay in the camera vertical deflection
system so that no delay networks are required to time the vertical pulses properly. It will
be noted that the output of each studio camera is brought to a bank of switching relays as-
sociated with that studio and located at the master control position. These relay switch-
ing banks in turn feed isolation amplifiers which are arranged to feed banks of relays con-
necting the studio outputs to the line amplifier inputs. Each line amplifier provides two
PULSE MEASUREMENTS 20-33
outputs, one of which can be patched to feed the transmitter and the other can provide a
monitoring return-feed to one of the studios.
Normally, only one or two of the amplifiers (regular and spare) will be used for feeding
the picture transmitter. The other line amplifiers are patched to provide monitoring feeds
for the studio control rooms, announcers' booths, clients' booths, or other points in the
television plant where line-fed monitors are used. As indicated, coaxial patch cords in
connection with coaxial jacks are provided so that changes in system interconnections can
be rapidly effected as dictated by operating requirements. In addition, a number of spare
coaxial cables connecting to each studio terminate in a jack-field adjacent to the master
control console. This makes it possible to patch up special circuit arrangements as re-
quired. Means are also provided for patching up special control circuits. For example,
the effects studio output, which may be a picture of a title slide, can be patched into one
of the spare camera relays in the relay bank associated with the direct pick-up studio.
Thus the video operator in the direct pick-up studio merely presses a camera switching
button when he wishes to insert the slide in the outgoing program.
The master control position is equipped with picture and wave-form monitoring facil-
ities, a television receiver used as an off-the-air monitor, and audio monitoring equipment.
The master control desk is normally equipped with a pushbutton-controlled monitoring
system so that the incoming picture from any of the sources can be checked as required.
A wave-form monitor associated with the picture monitor is used for checking signal levels,
pulse wave forms, etc. All program switching between the various signal sources and the
transmitter is done at the master control position.
A control unit for handling remote pick-ups consisting of a picture monitor, a wave-
form monitor, and a variable gain video amplifier is usually provided. The output of this
unit feeds into one of the relays in the line amplifier bank as shown. A relay is also pro-
vided to open the line amplifier synchronizing signal input when the remote relay closes,
as the remote signal normally arrives complete with synchronizing signals. When the
remote synchronizing generator is locked-in with the same power supply as the main
generator, it is possible to adjust the phase of the two synchronizing signals so that the
rapid switch from local to remote pick-up causes no appreciable disturbance of receiver
scanning.
Conventional relay interlock systems are used to prevent closing of more than one relay
in a particular bank at any time and to drop out one relay when the next is picked up.
Magnetic delay circuits can be arranged to delay the drop-out of one relay until just before
the next closes.
A wide variety of electronic fading and switching systems may be used in addition to the
relay system shown. Fades, lap dissolves, superposition of one image on another, in
whole or in part, may be accomplished electronically.
SYNCHRONIZING GENERATOR. Electronic synchronizing signal generators,
rather than electromechanical generators, are almost universally used for providing the
pulses needed to operate the television plant. The type generally used (reference 27)
incorporates an AFC oscillator operating at double line frequency in connection with a
frequency divider having an output at field frequency. The output of a discriminator
comparing the local 60-cycle power frequency with the output of the frequency divider
controls the AFC oscillator. By means of a number of multivibrators, delay networks,
and pulse shaping networks, the generator provides the following outputs: (1) synchroniz-
ing signals; (2) line-frequency driving pulses; (3) field-frequency driving pulses; (4) camera
blanking signals; (5) picture blanking signals. Controls are provided for regulating the
duration times or "widths" of the various pulses. The relative starting times of the
various pulses are usually controlled by means of an electrical delay network incorporated
within the unit. The outputs of the synchronizing generator are normally available at
peak-to-peak voltages of 4 to 6 volts at an impedance of 75 ohms.
The general practice has been to use the local 60-cycle power source for locking-in the
synchronizing generator. However, some designs incorporate a selector switch for locking
the synchronizing generator in either with the local power frequency or with a subharmonic
of a crystal oscillator. Operation of the synchronizing generator from a stabilized fre-
quency source independent of the local 60-cycle power mains has many advantages.
18. PULSE MEASUREMENTS
In order to insure that the transmitted blanking and synchronizing pulse wave forms con-
form to the FCC standards', the television broadcasting plant must be provided with test
equipment for measurement of the relative starting times, slopes, and duration times of
these pulses.
20-34
TELEVISION
Space does not permit a discussion of the great variety of measurement techniques that
can be or have been successfully used. However, the following have been found to be
convenient and are sufficiently accurate for practical purposes (reference 35) :
SINE-WAVE SWEEP. A method that allows rapid and accurate checks to be made
of pulse slopes, widths, and delay times utilizes an oscilloscope with sine-wave sweep of
110-
140-
FIG. 9. Alignment Chart for Pulse Width, Scope, and Relative Time Delay Measurements Using
Sine Wave Horizontal Sweep
either line or field scanning frequency depending on the character of the pulse to be meas-
ured (reference 35). The line-frequency sine wave is obtained by filtering out the fun-
damental of the horizontal pulses from either the synchronizing signal, the picture or
camera blanking signals, or the horizontal driving pulses. For accurate results, the sine
wave used for measurement purposes should be well filtered so that the arithmetic sum of
OVERALL VIDEO SYSTEM RESPONSE 20-35
all ^ harmonics does not exceed 1 per cent. The local 60-cyele a-c mains, filtered as re-
quired, may be used as a source of field-frequency sine wave if the field frequency is locked
in with the local power source. The oscilloscope used should have a linear horizontal
sweep width of about 100 mm minimum. Pulse widths are measured by shifting the pulse
to the center of the screen by means of a sweep phase shifter and measuring the dimensions
indicated on Fig. 9 with a transparent millimeter scale at the 10 and 90 per cent amplitude
points of the wave.
The width of the pulse in percentage of a sine wave period may then be obtained from
the nomographic chart. The expanded scale should be used for widths of less than 3 per
cent. Pulse slopes are measured by shifting the pulse edge in question to the center of the
screen so that the 10 and 90 per cent amplitude points are symmetrically disposed about
the center line of the sweep and scaling C or CA and D. The C dimension appears mag-
nified compared to linear sweep when sine wave is used, and the accuracy of measurement
is thereby enhanced. Pulse delay times may be measured with respect to a specific time
(such as the starting time of horizontal blanking) by shifting the phase of the sweep until
the starting time of horizontal blanking and the starting time of the pulse in question ap-
pear symmetrically disposed about the center line of the horizontal sweep. C and D may
then be scaled off and the relative delay in percentage of a horizontal scanning period read
from the chart. The delay time of a network may be similarly measured by comparing
the difference in position on the sweep of an input and output test pulse.
A variation of the sine-wave method uses an accurate phase shifter calibrated in per-
centage of a scanning period. This does away with chart and millimeter scales, and the
linearity of horizontal sweep of the oscilloscope is no longer a factor as slopes and widths
may be read off by shifting the wave known amounts with respect to a fine vertical line
drawn down the center of the oscilloscope screen.
PULSE CROSS METHOD. The number of vertical synchronizing signal sections,
the number of equalizing impulses before and after the vertical synchronizing impulse,
and the approximate widths of the synchronizing and blanking signals may be determined
by the pulse cross method (reference 35). These determinations are accomplished by
locking in the picture monitor with horizontal and vertical pulses which have been delayed
half a period and reversing the polarity of the composite video input signal. The pulse
and blanking signals then appear as a white cross in the center of the picture tube screen.
The items mentioned above may then be determined by measurement and observation of
this pattern. The vertical deflection amplitude should be expanded by about 3 : 1 while
making this test. A simple switching arrangement can be arranged to shift the picture
monitor from normal to pulse cross operation rapidly during operation.
19. OVERALL VIDEO SYSTEM RESPONSE
In the usual television plant the picture signals pass through a relatively large number of
amplifier stages in cascade in traveling from the camera to the transmitter. The transient
response of the overall system must therefore be given careful consideration. A small
phase or amplitude distortion in each individual stage has a cumulative effect when a
large number of stages is operated in cascade (reference 39). The overall effect of such
distortion when not compensated is to cause transients of an oscillatory nature to occur
whenever the scanning spot encounters an abrupt change in scene brightness.
Mathematical analysis of the overall transient characteristics of a practical system is
not only difficult but is complicated by the fact that all stages will not ordinarily use
identical forms of high-frequency compensation or peaking. A practical engineering ap-
proach to the problem which yields a satisfactory solution is the following: (a) When laying
out the plant, an accurate estimate can be made of the number of stages likely to be con-
nected in cascade. This estimate can be used in conjunction with published data (refer-
ence 39) to decide on reasonable values of design parameters for high-frequency com-
pensation of individual stages. (6) The design parameters for high-frequency video com-
pensation having been chosen, the time delay distortion, due to a number of stages in cas-
cade, can be calculated. If the difference in transmission time between medium fre-
quencies (100 to 200 kc) and high frequencies (5 Me) for the number of stages in cascade
begins to approach an appreciable fraction of the time of one picture element, then it is
advisable either to choose other design parameters giving smaller time delay distortion
per stage or to employ a properly designed phase compensation network, (c) It is ad-
visable to choose video amplifier design parameters such that the overall video amplitude
response will be uniform within ±1 db. This can be accomplished by choosing a top video
frequency (for design purposes) somewhat higher than the nominal top frequency handled
by the transmitter. Thus, the studio equipment amplifiers might be designed and com-
20-36
TELEVISION
pensated for a top frequency of 6 Me to assure uniform overall amplitude characteristics
up to the 4.5-Mc nominal top frequency dictated by present standards. When this is
done, however, care should be taken that there are no appreciable peaks in the amplitude
response beyond 4.5 Me. A gradual decay in amplitude response beyond 4.5 Me rather
than an abrupt change is desirable, (d) The low-frequency compensation of the video
system (60 cycles to 100 kc) should follow conventional principles, considering the number
of amplifier stages in cascade, (e) Having observed the above design precautions and pro-
vided a system having uniform amplitude response (within ±1 db) from 60 cycles to 4.5
or more megacycles, the overall transient characteristics of the system should be investi-
gated experimentally by square-wave techniques. The low-frequency transient response
may be investigated by means of 60-cycle square waves. The high-frequency transient
response may be investigated using steep-sided square waves of a fundamental frequency
of 100 kc (reference 42) . The 100-kc square wave should be of sufficient steepness to repre-
sent harmonics of 100 kc beyond the cut-off frequency of the system. The equivalent
phase and amplitude characteristics of the system may be obtained from the square-wave
response wave shape either by mathematical analysis or by means of special charts (refer-
ence 40) . Appropriate phase and amplitude correction networks may be designed on the
basis of square-wave test data.
Standards should be set as to the maximum allowable amount of overshoot and follow-
ing transients that can be tolerated in the square-wave response characteristics of a tele-
vision broadcast system. In any specific case, however, one can form an opinion as to
whether objectionable transient effects exist by observing the television image, preferably
an image of a resolution test pattern having a number of sharply defined boundaries of
high difference in contrast. An overshoot or oscillatory transient differing by 2 per cent
from the final steady-state value of a square wave will normally be noticeable in the image.
20. TELEVISION FIELD PICK-UP EQUIPMENT
From the electrical standpoint, television field pick-up equipment is quite similar to
studio equipment, the major circuit functions being identical. Mechanically, however,
the equipment is usually segregated into small, light-weight units of suitcase style so that
it may be readily transported (reference 44) .
A block diagram of a typical complement of field pick-up equipment for two cameras is
given in Fig. 10.
-115 v 60 co a-c
Sync.
115 v_^
generator unit
60 w a-c
and
power supply
: I
: i
; i
; i
Pulse shape
115 v_^
60 w a-c
and delay unit
and
power supply
•VSync. signals
-^.Driving pulses
—>- Video signal
Composite signal
Camera control
unit 1 with
picture and
CRO monitors,
Camera 1
Camera control
unit 2 with
picture and
CRO monitors
Camera 2
— -
-jfc
t
Regulated
power supply
Master switehlnff
115v_
60 cu a-c
115 v_
60 w a-c
unit and
video line amp.
^Reg, line out
i«« »>>-Emg. line out
^•Mon. out
Regulated
power supply
1
1
Radio relay rnoru In
FIG. 10. Block Diagram of a Typical Complement of Portable Field Equipment for Two-came:
Operation
RELAY OF TELEVISION SIGNAL
20-37
FIG. 11. Typical Construction of a Coaxial Cable Using a
Minimum Amount of Solid Dielectric
21. RELAY OF TELEVISION SIGNAL
Television network facilities may be classified as "intercity" and "local." Under the
first category are included long-distance coaxial carrier cables and radio relay multilink
circuits. The latter class includes
existing telephone pairs and special
shielded television pairs, video co-
axial cables, and short-haul micro- External shield
wave radio pick-up links.
INTERCITY TELEVISION FA-
CILITIES. Coaxial cables (refer-
ences 45 and 46) . The long-distance
coaxial cables consist of several co-
axials enclosed in a lead sheath
along with ordinary paper-insu-
lated telephone pairs. A 3/s-in.
longitudinal seam coaxial is com-
mon, although 0.27-in. coaxials
have also been used. Figure 11
pictures a coaxial unit open at the
end to show the construction. See
also Section 10.
Figure 12 shows the characteristic impedance, the phase delay, and the attenuation of
3/s-in. coaxials. The useful frequency range for television purposes on such a system de-
pends upon the type and spacing of
the repeaters. The present coaxial
system employs repeaters at approxi-
mately 8-mile intervals and transmits
television with a 311-kc carrier up to
about 3.1 Me, giving a 2.8-Mc video
band. These lines must be carefully
equalized for gain and delay character-
istics. Figure 13 shows overall char-
acteristics obtained (1946) on the New
York- Washington coaxial system.
Transmission of television signals
over local video facilities is direct; i.e.,
the entire band of frequencies pro-
duced by the television camera from
a few cycles per second to high fre-
quencies is transmitted directly over
the line. On long-distance coaxial
facilities, however, a carrier method of
transmission is used to avoid the
effects of low-frequency interference.
By using a relatively low carrier fre-
quency and vestigial sideband trans-
mission, the band-width requirements
of the repeaters are not materially in-
creased over a noncarrier system.
Figure 14 illustrates a typical carrier
transmission system for a 2.8-Mc pass
band in which a dual modulation and
demodulation process is utilized.
Only the frequencies above about
200 kc are used to transmit the tele-
vision signal over the line, although
the space below 200 kc may be
used for the accompanying sound-
program channel. The main reason
5000 for not using very low frequencies
Frequency - kc per second is that such coaxial systems would
FIG. 12. Transmission Characteristics of a Coaxial Cable |?e noisy and difficult to equalize
Constructed as in Fig. 11 (outside diameter, 3/8inch) In the frequency range used, coaxial
78
77
76
75
74
s,
Z = F
?+^
"*•>•
v^
"^
•*-^.
"--»
-•— ^.
/
*
Te
TIP
, s
= 5!
1
/
/
/
'
/
/
''
^
S
'
-^
*^^
50 70 100 200 500 1000 2000 50(
20-38
TELEVISION
systems are extremely quiet and relatively easy to equalize. For very long distances, the
cost and complexity of the terminal apparatus are small compared to those of the rest of
the circuit, but for short video facilities they might be objectionable.
+6
42
%
• o
O -2
-6
-8
+10
I-1S
'•-IS
'has1 s devatiqn frcjm'll(ie6rl:
; deviation froi
400 800
1200 1600 2000 2400 2800 3200
Frequency • kc
. FIG. 13. Overall Characteristics of the New York-Washington Coaxial Circuit (1946)
Microwave Radio Relay (reference 47) . Multilink radio relay systems also provide an
important network facility for the transmission of television programs. No general rules
can be given governing the choice between coaxial cable and radio relay, however, as each
specific installation must be carefully studied from a number of standpoints. Among
the factors governing such a choice, economic considerations will usually be paramount.
Such questions as relative operating and maintenance costs and network reliability must
Transmitting terminal
First modulation
Video signal band
Lower sidebar^
(transmit!
Vestigial sideband %
(partially transmitted)
UPP
S
'estigial sideband
Lower sideband
Transmitted to line
4.945
7.945
First carrier
er sideband*)
uppressed-H
1
Second modulation
10.945
Upper sideband
13.201 to 16.201
(suppressed)
8.256
Second carrier
Receiving terminal
First demodulation
: Upper sideband J
(Suppressed)
2.8|
45678
Frequency In megacycles per second
11
12
FIG. 14. Diagram of a Typical Dual Modulation and Demodulation Process Used for Transmission
of a 2.8 Megacycle Video Band over a Long Coaxial Cable
also be considered for each installation: Figure 15 indicates the repeater gains required
for both methods of transmission assuming a useful band width of 5 Me. It will be noted
that, except for extremely large-diameter coaxial cable, fewer repeaters are necessary for
the radio relay system. This figure also illustrates the reduction in repeater gain which
may be effected by employing the higher frequencies in the microwave region when a given
size antenna reflector is used.
RELAY OF TELEVISION SIGNAL
20-39
160
LOCAL TELEVISION CIRCUIT FACILITIES. Various local television transmission
facilities may include ordinary telephone pairs, specially designed shielded pairs, coaxial
cables, or microwave radio sys-
tems. Intracity wire transmis-
sion of television is accom-
plished at video frequencies
thus avoiding the use of carrier
terminals for the short dis-
tances encountered.
Telephone Pairs (references
45 and 46). Typical transmis-
sion characteristics of tele-
phone pairs are shown in Fig.
16. Because of the large at-
tenuation of the higher video
frequencies, it is necessary to
install suitable amplifiers at
spacings of an average length
of 1 mile, though this interval
may be increased somewhat
when the larger gages are em-
ployed.
It is necessary to equalize the
attenuation and phase charac-
teristic vs. frequency of the
telephone pairs over the video
band of frequencies. This is
accomplished by means of vari-
able equalizers associated with
each video amplifier. Pre-em-
phasis of the level of the higher
video frequencies is usually em-
ployed in these transmission
circuits to obtain an improved
15 20
Repeater spacing-miles
signal-to-noise ratio.
Comparative Repeater Spacings and Gains for Coaxial
and Microwave Circuits
FIG. 15.
Other factors to be consid-
ered in the use of telephone pairs for video transmission are the selection of suitable
pairs within the cables and the removal of bridged taps on the pair selected. The selection
of pairs within a chosen cable sheath is made with a view toward reducing interference
20 40 60 80100 200 400 600 1000 2000 4000-
Frequency In kilocycles per second
FIG. 16. Insertion Loss of Various Types of Telephone Pairs for Video Frequencies
from adjacent circuits and to avoid cross-talk coupling around the video repeater. An
bridged taps are removed to assure minimum imped-knce irregularities due to these lumped
constants along the lines.
20-40
TELEVISION
Shielded Pairs. Where it is desirable to extend the length of the wire circuit between
video repeaters, the use of special shielded pair is indicated. An opened section of such a
cable is shown in Fig. 17. The transmission characteristics of such a shielded pair are
FIG. 17. Low Loss Balanced Shielded Video Transmission Line
given in Fig. 18. With this pair it is possible to extend the video repeater spacing to ap-
proximately 3.5 miles.
This type of cable consists of a pair of No. 16 gage wires insulated and spaced by means
of polyethylene strings. This core is then enclosed within a cylindrical shield formed with
metal tapes. A number of these units may be enclosed in a lead sheath, or the shielded
pair unit may be inserted in an
ordinary telephone cable re-
placing a certain number of the
usual paper-insulated pairs.
Coaxial Cable (references 45
and 46) . Although of primary
importance for network facili-
ties, coaxial cable may be used
for intracity circuits of a more
permanent nature, such as stu-
dio-transmitter link service.
For short distances, transmis-
sion of the video signals with-
out utilizing a carrier system is
practicable. The inherent un-
balanced properties of the co-
axial cable, however, usually
re that special low-fre-
quency balancing circuits be
employed. A typical "hum"
balancing circuit is shown in
16
14
12
10
3
6
4
2
0
/
/
/
/
/
/
s
'
'
^
^
^~
.-.-•
.^-^
50 70 100 200 500 1000 2000 5QC
Frequency-kc per second
FIG. 18. Attenuation Characteristics of the Line Illustrated in
Fig. 17
Fig. 19. Included in this figure is a simulated generator of low-frequency interference.
It will be noted that noise current components flow in opposite directions through the cable
terminating resistor RI and the hum balancing potentiometer R2. By adjustment of the
balancing potentiometer, a condition can be found such that equal and opposite noise
voltages are developed between points a-b and points b-c. The noise is thereby reduced
--j" conductor
InsuJated from shield
r—ty—— ------
5 PCoaxiaJ cable grounded at
r^ j Input terminal only
'^Balancing potentiometer
Jd
•=• Local ground at output
Sunulated Interference generator termina' °f Cab'e
FIG. 19. Hum Balancing System for a Coaxial Cable Having an External Lead Sheath Insulated
from the Copper Outer Conductor
at the input of the amplifier so that the signal voltages alone are applied between the
grid and cathode of V\.
Equalization of transmission of coaxial cables is usually accomplished by the use of an
equalizing network inserted between the cable and the input of the receiving video amplifier.
TRANSMITTER PLANT TERMINAL EQUIPMENT 20-41
In certain^ applications where coaxial and balanced transmission facilities are to be con-
nected, special amplifier circuits or wide-band video repeating coils are employed to make
the transition.
Microwave Radio Relay. Microwave radio relay is also an important local facility
for video transmission. Many television field programs, such as parades and special
events broadcasts, are not repeated at frequent enough intervals from a given location to
justify the expense of wire facility installations. Furthermore, programs originating at
distances greater than 20 miles from the studio plant are usually more economically handled
by radio relay. Proper evaluation of these and related factors is necessary to determine
the choice between radio relay or wire facilities. Radio relay may also be employed for
studio-transmitter link service.
The power requirements for a microwave relay system may be approximated by the
following formula. Although accurate only for the free-space propagation condition,
application of this formula in practice where line of sight exists will yield results of suf-
ficient accuracy to be useful. It should be noted that the maximum total received power
due to ground reinforcement can approach, as a limit, four times the received power for
free-space propagation as obtained from the formula.
The free-space transmission formula is (reference 48) :
-r-o-
where Pt = power fed to transmitting antenna at input terminals 1 «
pr = power available at output terminals of receiving antenna/ um
Ar — effective area of receiving antenna
At = effective area of transmitting antenna
d — distance between antennas
Same units
X ss wavelength
The power necessary at the receiving antenna output terminals depends, among other
factors, upon the signal-to-noise ratio requirements of the relay system. The noise level
due to thermal agitation at 20 deg cent may be computed from the following expression
(reference 47) :
Pn = (0.8 X 10~20) (5) (6)
where Pn = noise power in watts due to thermal agitation.
B =* twice the highest modulation frequency in cycles per second.
In practice, the noise level due to all equipment causes will usually be between 10 and 15
db above thermal.
The effective area of an antenna is directly proportional to the power gain. The follow-
ing tabulations indicate the effective areas of several typical antennas.
ANTENNA EFFECTIVE AREA
Isotrot)ic radiator \z/4-7r
Half-wave dipole 0. 1305X2
Parabolic reflector Two-thirds of the projected
area of the paraboloid
Several factors affect the effective area of a paraboloid, the most important being the
efficiency of excitation. For example, the effective area is reduced to approximately
three-eighths of the projected area when only half of the exciting antenna energy is directed
toward the reflector. If transmission lines or wave guides are used in the antenna system,
the attenuation due to these components should be taken into consideration when apply-
ing the free-space-transmission formula.
22. TRANSMITTER PLANT TERMINAL EQUIPMENT
Terminal equipment located at the television transmitting plant performs the function
of raising the signal level delivered by the program source to that required by the trans-
mitter and provides the necessary picture and wave-form monitoring facilities. The equip-
ment is usually installed in a shielded room; it may consist of the following units:
A. An amplifier with means of controlling the composite signal amplitude.
B. An amplifier with independent amplitude control of the synchronizing and picture
portions of the composite video signal.
C. Video switching system to select one of several sources of signal.
D. A line amplifier of sufficient output to meet the input level requirements of the video
section of the transmitter.
20-42
TELEVISION
B. Picture and wave-form monitors.
F. Monitor switching system to select circuits to be monitored.
Figure 20 shows a simplified block diagram of the visual portion of a typical television
transmitter plant. Equipment required for the television sound channel follows standard
frequency-modulation broadcasting practice.
VISUAL CARRIER FREQUENCY GENERATION. The r-f carrier signal for a tele-
vision transmitter is generally developed by conventional methods. The primary source
of radio-frequency energy is usually a highly stabilized quartz-crystal oscillator operated
at a relatively low frequency. This low-frequency, low-power signal is multiplied and
From relay
facility
FIG. 20. Picture Transmitter Block Diagram Showing Video Input Equipment
amplified to the frequency and power level required at the modulated amplifier stage of
the transmitter.
MODULATION METHOD. A few of the many possible methods of modulating the
visual carrier (reference 49) are illustrated in Fig, 21. Of these, grid-bias modulation is
almost universally used.
Modulation may be either at low or high r-f level. At low level the grid-bias-modulated
r-f amplifier is followed by one or more class B linear r-f amplifier stages having the re-
quired band-pass characteristics.
MODULATED AMPLIFIER. The plate and grid (if grid-bias modulation is used) tank
circuits of the modulated amplifier as well as all succeeding r-f stages must be capable of
passing the generated sideband power without excessive amplitude or phase distortion.
This requires tank circuits of relatively low impedance resulting in rather poor operating
efficiencies as compared to sound transmitters.
NEUTRALIZATION. The band-pass characteristic of a television transmitter using
triode tubes depends not only upon the circuit elements but also upon the effectiveness of
neutralization. At low frequencies, where lead inductances may be neglected, a simple
capacitance bridge adequately represents the neutralizing circuits. At higher frequencies,
however, where lead inductances become appreciable, additional compensation is usually
necessary, especially for wide-band operation. Figure 22 indicates the stray inductances
often encountered and methods of compensation (reference 50) . Stray or undesired cou-
pling between input and output circuits not only disturbs neutralization but also affects
the band-pass characteristics of the amplifier.
TRANSMITTER PLANT TERMINAL EQUIPMENT 20-43
D-C TRANSMISSION. According to 1946 standards, the tips of the synchronizing
signals correspond to maximum carrier envelope amplitude, and this is held as nearly con-
stant as possible during a given transmission. Black level, which corresponds to the base
of the synchronizing pulses, is maintained at a fixed percentage of the maximum carrier
envelope amplitude within narrow tolerance independent of the values of light and shade
in the picture transmitted. In order to achieve this result one or more of the various forms
of "d-c restoration" circuits are used in the modulator stages of the transmitter. (See
article 7.)
Modulator
Grid-modulated r-f amplifier
Grid-bias modulation
Plate-modulated r-f amplifier
Modulator
Plate modulation
R-f amplifier L 90° at
4M,
^J^F^
to
^_
output
O
t
T
<j>
-,-
L
Load Impedance modulation
FIG. 21. Video Modulation Methods for Amplitude Modulation
VESTIGIAL SIDEBAND TRANSMISSION. A vestigial sideband system of television
transmission (reference 51) is standard for commercial television broadcasting. The
higher-frequency sideband components up to but not in excess of carrier plus 4.5 Me and
the lower-frequency sideband components down to carrier frequency —0.75 Me are trans-
mitted. The remainder of the low sideband energy must be attenuated as rapidly as
possible and must reach and retain a low order of magnitude at frequencies lower than
carrier frequency —1.25 Me. Curve C of Fig. 20, article 9 r illustrates the standard
vestigial sideband transmission characteristic.
Transmitters which are modulated at high power level must be followed by a vestigial
sideband filter which absorbs the developed but undesired sideband energy (reference
52) . Vestigial sideband filters employ various configurations of elements and are usually
constructed in the form of sections of concentric transmission lines of suitable lengths,
diameters, and diameter ratios. A single section of one type of vestigial sideband filter
is shown schematically in Fig. 23. Generally, two or more sections of this type of filter
are used. In addition, "notching" filters are often required to provide additional at-
tenuation at the low-frequency edge of the assigned channel.
Transmitters which are modulated at low power level may achieve the required trans-
mission characteristics by proper design and adjustment of the interstage coupling net-
works of the following linear amplifiers. In this case, a less pretentious vestigial sideband
filter may be necessary at the output of this type of transmitter in order to achieve the
required characteristic.
20-44
TELEVISION
{ RADIO-FREQUENCY M ONITORING. Since the output of a vestigial sideband trans-
mission system is viewed on receivers having specified band-pass characteristics, a mon-
Brldge neutralization
Indicating disturbing
self-inductances
CN
1 — ir-
G,c=£
— ^
f , T
f +i
T f-wv
IGni 1— i
Basic circuit
CM
Bridge neutralization
Indicating compensation
of disturbing Inductances
by capacitors Cr Ca/ and C8
FIG. 22. Neutralization Method to Compensate for Stray Inductance
itor should be provided which not only conforms to the standard receiver characteristic
but also yields a signal that is a true sample of the radiated energy from the transmitter.
The aural transmitter may be monitored with equipment similar to that developed for
the frequency-modulation broadcast serv-
ice.
MODULATION MEASUREMENT.
The modulation of the television trans-
mitter may be measured in various ways,
but the methods that take advantage of
the fact that a television transmitter is
operated at a constant peak carrier level
have been found most satisfactory in
practice.
Since the tips of the synchronizing
signals represent 100 per cent modula-
tion, one relatively simple method is to
observe the carrier envelope pattern at
radio frequency on an oscilloscope as
shown in Fig. 24. At the high carrier
FIG. 23. Single Section Vestigial Sideband Filter
frequencies involved, however, it is sometimes difficult to insure that the cathode-ray
pattern is a true representation of the developed carrier envelope amplitude.
TRANSMITTER PLANT TERMINAL EQUIPMENT 20-45
A method which avoids dealing with the radio frequency directly utilizes the output of a
linear rectifier applied to the vertical plates of the oscilloscope, normal sawtooth sweep of
a convenient frequency being used for horizontal deflection. A contactor is provided to
short-circuit the output of the diode periodically. This provides a reference level cor-
responding to complete modulation in the white direction, or zero carrier envelope am-
plitude. The modulation percentage may be scaled off the cathode-ray screen as in-
dicated in Fig. 24 which shows the appearance of the pattern using high frequency sweep.
This simple method is quite accurate and may be utilized periodically as a visual operating
check of transmitter modulation during a program (reference 53) .
Carrier envelope
H
orlzontal sync
r— pulse
/ j
I
110
**,
L
*T
\l I
r,
2
Time — ^
Horizontal sync
1 T.X pulse
Zero reference
(Contactor closed)
<{
FIG. 24. Video Modulation Measurement, (a) Oscilloscope presentation of video modulated RF
envelope (HF sweep). (6) Oscilloscope presentation of output of linear detector with shorting con-
tactor (HF sweep).
MEASUREMENT OF R-F OUTPUT POWER. Television transmitters are rated in
peak power output, i.e., the power output level attained during the synchronizing pulse
portion of the transmitted signals.
The following methods of measuring power output assume that the transmitter power
output can be held at the operating peak level. For transmitters that cannot be held at
peak output for measurement purposes, other methods have to be used or a reliable cor-
rection factor must be applied.
The transmitter output power may be determined by measuring the power delivered
to a water-cooled resistance load with circuit adjustments capable of transmitting a good
picture. The rate of water flow and the temperature rise of the water stream on passing
over the resistor must be accurately measured. Then the power delivered is given by
P = 2QZTF (7)
where P = power delivered to load in watts.
T = temperature change of water in degrees centigrade.
F = water flow in gallons per minute.
It is often desirable to know the power delivered to the actual operating load. Since
most practical transmission line installations are not perfectly matched to the radiator,
a finite reflection occurs on the line. It is, therefore, necessary to determine the average
value of transmission line voltage. One satisfactory method utilizes a slotted section of
transmission line and a calibrated vacuum-tube voltmeter for determining the maximum
and minimum values of the transmission line voltage.
The power delivered to the transmission line load, neglecting line attenuation, may be
20-46 TELEVISION
calculated by means of the following formula, which is accurate to better than 1 per cent
if the voltage standing wave ratio is between 0.8 and unity.
ln)
where Po = power delivered to load in watts.
jEWx = rms value of voltage maximum in volts.
•#mfn ~ rms value of voltage minimum in volts.
ZQ = characteristic impedance of transmission, line in ohms.
Alternatively, the output power may be determined by permanently locating two cal-
ibrated vacuum-tube voltmeters precisely one-quarter wavelength (electrical) apart and
substituting the voltage indicated by these meters for jE/max and j&min in the above formula.
TRANSMISSION LINE. The transmission line system between the transmitter and
the antenna must be well matched over the band of frequencies which includes the carrier
and the sideband frequencies of appreciable magnitude. Multiple images may appear
in the radiated signal of a poorly matched transmission system. Satisfactory results are
usually produced when a standing wave ratio between 0.9 and 1.0 over the required band
of frequencies exists.
ANTENNAS. Commercial television broadcasting antennas are required to be hori-
zontally polarized. The directivity and radiating efficiency of the antenna should be sub-
stantially independent of frequency over the desired transmission band. The input im-
pedance of the antenna must be substantially independent of frequency and must match
the transmission line well enough to avoid the development and transmission of multiple
images (references 54 and 55) . Appreciable effective power gain may be obtained by com-
pressing the radiated energy in the vertical plane.
PERFORMANCE MEASUREMENTS. The response of the visual transmitter from
input to radio monitor may be measured using sinusoidal modulation. The modulating
frequency should be varied incrementally over the required band while the relative re-
sponse as a function of frequency is measured on a cathode-ray oscilloscope or vacuum-tube
voltmeter. Alternatively, the sinusoidal modulating signal may be injected in the studio
equipment before the blanking signals are added, and the relative response at the trans-
mitter input and at the radio monitor output may be measured on a cathode-ray oscillo-
scope. This method is applicable to transmitting systems which use d-c restoration cir-
cuits, and the results are representative of what may be expected under actual operating
conditions.
Means of observing and recording the transient response of a television transmission
system are desirable. If a 100-kc square wave, having a rise time which is short compared
to the rise time expected from the circuit under test, is applied to the transmitter the
transient response may be observed on a cathode-ray oscilloscope connected to a r-f mon-
itor. Some square-wave generators provide not only a 100-kc square-wave output but
also a synchronous 100-kc sinusoidal output and a synchronous 10- or 20-Mc output.
The 100-kc sinusoidal output may be advantageously used for horizontal deflection of the
measuring oscilloscope. The 20-Mc output may be used to modulate the cathode-ray
beam in amplitude. When the cathode-ray-tube bias is properly adjusted only the pos-
itive peaks of the 20-Mc modulation are visible, thus providing an accurate time base
which may be used to measure the change in amplitude of the signal for each accurate
time interval. The realized rise time, as well as the magnitude of overshoots or oscil-
latory transients, may thus be accurately determined. Such performance measure-
ments can generally be correlated directly with the appearance of the reproduced television
image.
TELEVISION RECEIVERS
By W. F. Bailey and R. J. Brunn
Receivers for television signals in accordance with the present-day standards of the
Federal Communications Commission are of the superheterodyne type and receive both
the picture and sound transmissions. A block diagram of a typical television receiver is
shown in Fig. 1.
The picture and sound carrier signals are received by a single antenna and are am-
plified in a single channel. The selectivity of this channel protects against image signal
and cross-modulation interference. Frequency conversion and some amplification at the
intermediate frequencies are also accomplished in a single channel. Then the picture and
sound signals are separated and each is amplified sufficiently for final detection. The
K-F CIRCUITS
20-47
selectivity in each channel must be adequate to keep the sound and picture signals from
interfering with each other, and also to attenuate adjacent signals to a non-interfering
Level. An f-m detector and an audio amplifier complete the sound channel.
In the picture channel, following the second detector, amplification occurs at video
frequency. Either direct coupling, or d-c restoration, or a combination, is used to main-
tain the voltage corresponding to black constant at the picture tube. In first-grade re-
ceivers, both automatic gain control and noise limiting are provided in the picture channel.
Synchronizing signals are extracted from the complete picture signal and are separated
for the respective scanning oscillators.
Scanning generators produce sawtooth waves at line and field frequency of either cur-
rent or voltage, depending on the type of picture tube. Magnetic deflection is commonly
used for best resolution since there is less defocusing than there is with electric deflection.
Transmission
line
rl
•*jj Loudspeaker
Picture
tube .f
|c=5r
Sound
amplifier
»
F-m
detector
-
A-f
amplifier
~ ampler * Modu"
Common J
or •» |.f
amplifier ~|
1 ( 1
Sound avc
1 Local
] oscillat
L
or
Picture
I-f
amplifier
*
Picture
detector
*
Video
amplifier
r n T 1
J Noise ij D-C
"Tf Hmiter y relnserter
1
Picture
automatic
tain control
^
1
"Synchroniz-J
Line
scanning
generator
*
] separator |1
Field
scanning
generator
Low
voltage
supply
High
voltaqe
supply
FIG. 1. Block Diagram of a Television Receiver
The d-c accelerating potential for the picture tube is obtained by rectifying the power-
frequency wave, an r-f sine wave, or the voltage impulse during the line retrace in a mag-
netic scanning system.
23. ANTENNAS
The usual antenna for reception is a half-wave dipole in which the radiator diameter is
from 0.2 to 2.5 per cent of the antenna length, to improve performance over the frequency
range. The folded dipole antenna (reference 55) is also used with a 300-ohm transmission
line. Some use has been made of a reflector to improve the directivity, but, with a simple
array, not much directive gain can be obtained over the frequency range.
Usually, a balanced line (reference 57) of 75 to 300 ohms impedance is used to transmit
the signal from the antenna to the receiver.
24. R-F CIRCUITS
REQUIREMENTS. The r-f circuits of a television receiver couple the signal from the
antenna transmission line to the modulator. The following factors must be considered in
the r-f circuit design: (1) r-f gain; (2) band width; (3) selectivity; (4) coupling to trans-
mission line; (5) station selection; (6) oscillator radiation; (7) noise factor.
R-F AMPLIFIER. Normally, it is not necessary to provide amplification at radio
frequency because it is easier to obtain the necessary amplification at intermediate fre-
quency. However, a,n r-f stage is helpful in reducing oscillator radiation (reference 58)
since there may be an attenuation of 10 to 50 times for signal propagation in the back-
ward direction through the r-f stage.
Most modulators have considerable noise (references 59 and 60) . The inherent noise of
the receiver may sometimes be reduced by use of an r~f stage (reference 61) . A triode r-f
amplifier will reduce the noise to the minimum. Generally, a pentode r-f amplifier will
provide no improvement. In order to eliminate the need for neutralization, the triode
is generally used in a grounded-grid circuit, and a tube having a low plate-to-cathode
capacitance is chosen.
20-48
TELEVISION
ANTENNA COUPLING. With a low-loss-transmission line, it is desirable that the
receiver input circuit match the line with a low standing wave ratio to eliminate ghosts in
the picture caused by multiple traversals of the transmission line (reference 62). The
antenna cannot be expected to terminate the line with a standing wave ratio lower than
about 10 db in some of the channels. Thus the reflection at the receiver must be kept low.
With 2-db attenuation in the line in one traversal, and an antenna termination with a 10-
db standing wave ratio, it is necessary that the receiver terminate the transmission line
with a standing wave ratio of 0.6 db so that the signal-to-ghost ratio in the receiver be 40
db.
A resistive element must be present in the receiver to achieve termination of the trans-
mission line with a low standing wave ratio. The input conductance of the first tube, the
Gang switch
FIG. 2. Typical Antenna to Modulator Coupling Circuits
inherent losses in the reactive circuit elements, and, in some cases, a resistor added for
the purpose, constitute the source of loading for the input circuit. The added resistor to
produce the required loading increases the noise factor above the minimum (reference 63).
To realize the benefit of the balanced line in minimizing extraneous pick-up, a coupling
circuit must be used between the transmission line and the first tube which has good
transmission for balanced signals and high attenuation for unbalanced signals. This will
reduce interference picked up by the transmission line acting as a single-wire antenna.
Transformers in which the electrostatic coupling is minimized are used to couple to the
balanced line. The secondary is usually unbalanced to deliver the signal to a single grid
or cathode. The transformer may be coupled directly into a cathode with a good im-
pedance match, but no selectivity.
SELECTIVITY REQUIREMENTS. Because the picture and sound carriers are at
opposite ends of a television channel, the r-f circuits should have substantially uniform
PICTURE I-F AMPLIFIER 20-49
transmission over a band width of about 5 Me. This is required because the sound car-
rier, the^main sideband, and the vestigial sideband should be amplified uniformly.
Sufficient selectivity should be provided to give an image ratio of at least 40 db. This
provides protection against image signals which are as strong as the desired signal. This
order of selectivity requires a minimum of two tuned circuits.
STATION SELECTION. Station selection may be accomplished by switching, with
fixed or movable coils, or by continuously adjustable inductors, using tuning cores, or by
varying the length of the wire to change the inductance.
The requirements for tuning are: (1) station selection by a single control; (2) reliable
long-life, noise-free operation; (3) provision for a number of channels lying between 4 and
12; (4) resett ability.
Some typical r-f circuits between the antenna transmission line and the modulator are
shown in Fig. 2 (references 64 and 65) .
25. MODULATOR AND LOCAL OSCILLATOR
MODULATOR. The tubes commonly used for the modulator are the triode and
pentode types. Multigrid converters are rarely used because of their high noise (refer-
ences 59 and 60) .
Because it has the lowest internal noise, the triode modulator is used when the best
noise factor is desired. However, the triode presents design problems, since both the in-
put and the output impedances are functions of the oscillator excitation, and the grid-to-
plate capacitance makes the input and output circuits interdependent.
The pentode modulator does not produce as low a noise factor because of the partition
noise. It is less difficult to use in the receiver, since there is negligible coupling between
the input and output circuits. Also, the output impedance of a pentode modulator is
normally so high that variations in it, caused by changes of oscillator excitation, have no
effect on the performance of the i-f amplifier.
A high transconductance tube is used to maintain high conversion gain and low noise.
It is usual to bias the modulator by drawing grid current on the local oscillator signal.
LOCAL OSCILLATOR. The local oscillator is usually a triode used with either capaci-
tive or inductive feedback. Capacitive feedback offers the advantages that the inherent
capacitances of the tube may be used directly in the oscillator circuit to produce feedback,
and that the tuning coil has no tap.
LOCAL OSCILLATOR DRIFT. Both the picture and sound quality suffer if the oscil-
lator varies from the correct frequency either by oscillator drift or poor resettability of
the tuning device. Frequency stability is of prime importance. A frequency shift of
±150 kc is about the upper limit that can be tolerated by the picture. This drift will
produce approximately ±2-db variation in the amplitude of low-frequency video com-
ponents relative to high-frequency components. The cost of the sound channel is increased
with high shifts. The sound-channel band width and the linear portion of the detector
characteristic must be adequate to accommodate the drift. Otherwise the sound i-f may
lie on the side of the i-f amplifier transmission characteristic. This produces amplitude
modulation of the f-m signal. Further, the performance of the frequency detector may
suffer, as the signal may be near one of the peaks and will be on a non-linear part of the
detector characteristic.
Receivers have frequently employed an oscillator tuning adjustment so that the reset-
tability errors of the station-selecting device and the oscillator drift can be corrected by
the user.
OSCILLATOR INJECTION. The oscillator signal is injected into the modulator grid
circuit by either magnetic or capacitive coupling. In many cases, the stray capacitance
of the station-selector circuit wiring is sufficient.
26. PICTURE I-F AMPLIFIER
The picture i-f amplifier provides most of the amplification required and also controls
the frequency band of the signal in the picture channel. The pass band varies in width
from about 2 Me in a low-definition receiver to about 4 Me in a high-definition receiver.
The i-f amplifier attenuates signals on the adjacent channels so that thes3 signals do not
interfere with the picture.
FREQUENCY. The choice of the frequency band for i-f amplification is governed
largely by interference from direct i-f pick-up and image signals. The local oscillator is
usually located on the high-frequency side of the signal as this simplifies the image inter-
20-50
TELEVISION
ference problem, and thus the picture intermediate frequency is higher than the sound
intermediate frequency. A choice of at least 20 Me for the sound intermediate frequency
eliminates other television stations as images, but the f-m broadcast stations are then in
the image-signal range. A choice of 29 Me or higher eliminates both television and f-m
broadcast stations as image signals.
The approximate frequencies of the i-f band are chosen with regard to image signals,
and the exact frequencies are chosen to eliminate serious interference by direct i-f pick-
up. Of the sources of strong signals in the bands cited above, amateur frequencies are
worst, since the transmitter may be close to the receiver.
Most current designs utilize a frequency of about 26 Me for the picture i-f carrier.
VESTIGIAL SIDEBAND REQUIREMENTS. For band-width conservation, picture
signals are transmitted by a vestigial sideband system (reference 66. See also article 9).
In this transmission system, it is necessary to attenuate the carrier frequency 6 db relative
to the transmission of the major sideband, and to adjust the transmission of both sidebands
adjacent to the carrier so that a uniform output-frequency spectrum results when a uni-
form input spectrum is applied to the system. This adjustment is made in the receiver.
In most receivers, the carrier and low video-frequency transmission is equalized prior
to detection as shown in terms of the r-f signal by B of Fig. 20, Article 9. Over a frequency
band of about 1.5 Me, the transmission drops from full value to 10 per cent or less, with
the cutoff characteristic so chosen that the carrier is transmitted at 50 per cent of full
transmission.
It is desirable that this cutoff characteristic be as gradual as the standards allow. This
reduces the distortion produced by the quadrature component (references 51, 22, and 23)
and the non-linear phase characteristic associated with the amplitude cutoff.
ATTENUATION CHARACTERISTIC. A typical picture i-f amplifier transmission
characteristic is shown in Fig. 3. The attenuation of the desired sound carrier, which is
23 24 25 26 27
Intermediate frequency, me
FIG. 3. Typical Receiver Picture I-f Response
28
normally obtained by the use of traps in the i-f coupling impedances, should not be too
steepsided, since a high cutoff slope will convert the sound-frequency modulation to am-
plitude modulation, which may show in the picture. The sound attenuation should be
about 300 kc wide, 3 db above the minimum, so that frequency drift of the local oscillator
will not cause sound interference in the picture.
It is desirable that about 40 to 50 db total attenuation be provided for the sound car-
rier. This may be produced entirely by i-f selectivity, or it may be obtained partly in the
i-f amplifier and partly by attenuation at 4.5 Me in the video amplifier.
Present station-assignment practice is such that adjacent channels will not be allocated
in any region. The overlapping service areas of any two regions whose allocations occupy
successive channels are small. Therefore, it appears reasonable to provide attenuations of
about 35 db minimum relative to the desired picture carrier for the adj acent channel carriers.
It is usually necessary to use traps to secure the attenuation at the sound carrier of the
lower-frequency adjacent channel.
COUPLING NETWORKS. Coupling networks used hi the i-f amplifier are of several
forms: double-tuned transformers (reference 67), filter-type networks, and stagger-tuned
resonant circuits are commonly used. See Section 7 for more information.
PICTURE I-F AMPLIFIER
20-51
Various methods are used to incorporate traps in the i-f amplifiers. Traps may be
part of the coupling impedance, or they may be used to reduce the effective transcon-
ductance of the amplifier tube.
Figure 4 shows several circuits in which traps are employed to reduce the transmission
in a desired frequency range. The transmission characteristics are also shown. Figure
4A shows a single stage in which a stagger-tuned single resonant circuit is used. The grid
leak of the following tube is chosen to provide the required Q. An inductively coupled
Frequency
Ji/a
Frequency
FIG. 4. Typical I-f Coupling Networks
Frequency
trap is used to secure attenuation at frequency /i. An undesirable feature of the in-
ductively coupled trap shown is the spurious response at frequency fz. The magnitude
of this spurious response is proportional to the Q and coupling of the trap, and its max-
imum can be substantially the same as the main response.
Figure 4B shows a single stage in which the coupling impedance is a section of an m-
derived filter. The response may be made uniform over the desired band with attenua-
tion at a specified frequency /i.
Figure 4C shows a single stage in which the coupling impedance is two coupled circuits.
To secure maximum gain, the damping is concentrated on one circuit only. Attenuation,
at frequency /i may be produced by a parallel resonant trap in the second tube cathode
circuit. Such a trap usually affects the input impedance of the tube because of feedback
to the grid circuit. It is undesirable to use cathode traps with tubes in which the sup-
pressor grid is connected to the cathode. As the cathode has considerable impedance to
ground, the suppressor-to-anode capacitance may couple sufficient signal from the output
circuit back to the input circuit to cause instability.
As the trap attenuation is a function of both the transconductance of the tube and the
impedance of the trap, cathode traps are normally employed in fixed-gain stages.
20-52
TELEVISION
GAIN CONTROL. Gain control is usually accomplished by varying the bias of one or
more i-f amplifier tubes. It is generally necessary, because of the use of high-trans con-
ductance tubes, and circuits in which the tube capacitance is a large part of the total ca-
pacitance, to stabilize the input capacitance of the gain-controlled stages by an unby-
passed cathode resistor (reference 68) .
27. PICTURE CHANNEL SECOND DETECTOR
The second detector in the picture channel is usually of the diode type. The video-
frequency output-signal load impedance is determined by the shunt capacitance of the
diode and the following stage and by the band width to be transmitted. If the impedance
band-width product is too low when the total capacitance is lumped as a single capacitor
to ground, then video-filter technique may be used. The total capacitance is then broken
up into several smaller units, allowing the impedance band-width product to be increased.
See Section 7.
DIODE LOAD. If the simple load circuit as shown in Fig. 5A is used, the rise time
for the video output signal for outward modulation of the carrier will generally be shorter
B *
FIG. 5. Picture Detector Circuits
than the fall time for inward modulation of the carrier. The diode and generator resist-
ance shunt the diode load time constant for outward modulation but not for inward modu-
lation.
If the diode load circuit comprises a filter network as shown in Fig. 5J5, the rise and fall
times of the video output signal are more nearly equal because they are determined by the
rate at which energy propagates through the filter network. The input should be at the
open end of the filter, since, with this connection, there is minimum reflection in the filter
which would affect the current supplied by the relatively low effective impedance of the
diode and i-f output circuit.
There may be variations in the charging time with the video modulating frequency,
since the output impedance of the i-f circuit driving the diode is not, in general, constant.
This effect is usually not serious.
TUBE CONSIDERATIONS. The diode load impedance is low, ranging from about
2000 to 8000 ohms. The output voltage generally ranges from about 1 to 5 volts, and this
results in high peak currents. To minimize the signal loss in the diode, it is thus desirable
to use a high-perveance tube with low interelectrode capacitance.
I-F HARMONIC INTERFERENCE. The use of a four-terminal diode load impedance
like that of Fig. 5B generally attenuates the ripple frequency component sufficiently so
that it, or its harmonics, do not produce spurious patterns in the picture. These i-f
harmonics can be troublesome on channels where they fall in the r-f picture frequency
band, if they are fed back to the r-f section of the receiver with sufficient level, as a beat-
frequency signal lying within the video-frequency passband of the receiver will then be
produced. A beat takes the form of alternate dark and light bands in the picture. Since
the beat signal is not related harmonically to the scanning rate, the bands continually
move about the picture. With full-wave rectification the fundamental ripple frequency
superposed on the video signal is twice the intermediate frequency and it is reduced in
amplitude, which simplifies the filtering.
OUTPUT POLARITY. The diode detector may be arranged to produce a video output
signal of either polarity. For the negatively modulated signals standardized in the United
States, the detector circuits of Fig. 5 will deliver video output signals of negative polarity;
that is, the synchronizing signals will be the most positive part of the video-frequency
output.
VIDEO AMPLIFIERS AND DISPLAY
20-53
28. VIDEO AMPLIFIERS AND DISPLAY
The video amplifier, in a television receiver, raises the level of the picture-detector out-
put signal to a satisfactory value for the picture tube. The input level is commonly about
1 to 5 volts peak-to-peak, and the output level ranges from about 20 to about 100 volts
peak-to-peak. It must be remembered that the signal range from black level to the
synchronizing-signal peaks does not contain picture information. Thus the video am-
plifier must handle a complete signal about 40 per cent larger than the black to white
signal. One or two stages of video-frequency amplification generally suffice in the usual
television receiver.
FREQUENCY REQUIREMENTS. The video amplifier transmits a wide band of fre-
quencies, one cutoff being at some low frequency, which may be direct current. The other
cutoff is at some high frequency, usually lying between about 2 and 4.5 Me, depending on
the desired resolution.
Direct coupling is difficult to use in a multistage amplifier because of the problem of
obtaining proper electrode potentials. It is simpler to design amplifiers whose lower
cutoff lies in the range of about 10 to 10,000 cycles per second. Effective transmission of
the d-c component of the signal may be accomplished by means of a locally generated d-c
component. This involves a d-c reinserter as described in article 7.
•B-f
. Two-stage Video Amplifier
-B-h
.B. Video Amplifier with D-c Reinserter
FIG. 6. Typical Video Amplifiers
In Fig. QA there is shown a two-stage video amplifier. D-c reinsertion is provided by
the high grid-cathode conductance for positive grid potentials of the second amplifier
tube. The picture tube is direct coupled to the output of the second video amplifier tube.
20-54 TELEVISION
A gain control which operates by varying the amount of negative regeneration for al-
ternating current is provided in the cathode circuit of the second stage. A change in gam
of about 6 to 1 may be obtained with uniform frequency response with a control of this
type. The rheostat should be non-inductive, and its range is limited by shunt capacitance
•which by-passes it for high video frequencies.
A potentiometer is sometimes used as an alternative gain control, in which the signal
on the arm of the control is supplied to the amplifier grid. In this case, shunt capacitance
to ground from the amplifier grid may vary the frequency response with gain-control
setting.
Figure 65 shows a circuit in which the signal is a-c coupled from the video amplifier to
the picture tube. A d-c reinserter is provided to stabilize the potential of synchronizing
signal peaks on the picture tube grid.
For d-c amplifiers or those using d-c reinserters on the input circuits, it is essential that
the amplifier stage have the same gain for direct current as for other frequencies within
its passband. This requires that the cathode, screen, and anode supply potentials be
stabilized against variation with varying direct current flowing in the amplifier tube.
Failure to meet this requirement means that the instantaneous brightness of any part of
the picture will be dependent upon the average brightness.
If the band width to be transmitted is not extreme, and the shunt capacitance not high,
a simple two-terminal constant-fc type of network is often used for a coupling impedance.
This type may be designed for quite uniform amplitude and phase characteristics. When
higher impedance is desired, or the circuit is required to work with high total shunt ca-
pacitance, it is common to use four-terminal networks. This type allows the shunt ca-
pacitance to be broken into .smaller lumps, thus giving a higher impedance-band width
product. For maximum exploitation of the band width, the circuit is designed as a filter
(reference 69). Such a filter, while it provides a maximum of uniform amplitude pass-
band, has a fairly sharp cutoff characteristic and a non-linear phase curve, both of which
may produce objectionable distortion in the form of echoes (reference 9) of the original
signal. In general, better performance is obtained with a network in which the amplitude
characteristic falls gradually with increasing frequency, as this reduces both the phase and
amplitude distortion. Section 7 gives more specific information regarding the design of
coupling impedances.
The video-frequency coupling network is generally designed to have uniform impedance
if it is of the two-terminal type, or uniform transfer impedance if it is of the four-terminal
type. Such designs give uniform gain if driven by high-impedance sources but do not
produce uniform gain if the driving source impedance approximates that of the network.
For the two-terminal type this is true because the network impedance is complex and has a
variable phase angle over the transmitted band. For the four-terminal type this is true
because, for uniform transfer impedance, the input impedance at the driving point is either
uniform in magnitude but complex with a variable phase angle over the transmitted band,
or non-uniform in both magnitude of impedance and phase over the transmitted band.
Normally, video amplifiers use the grid-cathode circuit for input, and the plate-cathode
circuit for output, and thus the signal polarity is reversed in going through a stage. In
the design of a receiver, the picture detector must be so poled that the desired polarity is
obtained at the picture tube grid.
PICTURE TUBE. The present-day picture tubes are of the cathode-ray type. The
electron beam is focused by an electron gun which may utilize electric fields only or a com-
bination of electric and magnetic fields. Deflection of the cathode-ray beam is produced
by either electric or magnetic fields. In the present state of the art, magnetic focus and
deflection appear to give the best performance in regard to: (1) spot size; (2) high current
in the beam; (3) uniformity of focus over the raster.
For direct-view receivers, the final anode voltages range from about 3 kv to about 15 kv.
For projection-type receivers, the final anode voltage in current designs is about 30 kv.
The phosphor produces a white light which may vary in shade from slightly bluish or
greenish to yellowish.
It is usual to provide a bias control to adjust the average brfghtness of the picture. Ex-
amples of this are shown in Fig. 6. Sufficient bleeder current flows through the bias con-
trol so the picture-tube current does not vary the bias appreciably, and a by-pass is pro-
vided for high-frequency currents.
Section 15 contains more detailed information on picture tubes.
PICTURE GAIN CONTROL. Automatic gain control for the picture channel is desir-
able in television receivers, as it minimizes readjustment of the controls when switching
from one channel to another. Badiated signals conforming to the FCC standards include
the d-c component. Thus, the average carrier level is dependent upon the picture content
as explained in articles 7 and 9. It is necessary that the automatic-gain-control circuit re-
NOISE LIMITERS
20-55
spond to a part of the signal which is independent of the transmitted picture. With a nega-
tive polarity signal, as prescribed by the FCC standards, it is most convenient to develop the
automatic-gain-control voltage from the synchronizing signal peaks. This requires that
the automatic-gain-control rectifier load circuit have a time constant of not less than sev-
eral lines duration, so that the picture content cannot affect the automatic-gain-control
voltage. A separate rectifier operated at the same level as the picture detector may be
used as the source of automatic-gain-control voltage. Better performance may be ob-
tained by amplifying the rectifier output voltage with a d-c amplifier. Figure 7 shows
~ -25 v
FIG. 7. Picture Automatic Gain Control Circuit
such an arrangement. In this circuit, Di is the picture detector; DZ is a separate diode
with a high-impedance load having a time constant of about 200 jusec. The output of D2
is direct coupled to a triode Fi, the cathode of which returns to a negative potential, in
this case, 25 volts. As the signal level increases, the anode of Y\ falls in potential, pro-
viding an amplified voltage which is suitable for an automatic-gain-control bias. An al-
ternative of this circuit may be used, in which the additional amplification occurs prior
to the automatic-gain-control rectifier. This amplification may take place at intermediate
frequency or video frequency.
29. NOISE LIMITERS
Noise Kmiters are sometimes used to reduce the effects of impulse noise interference
upon the picture-tube signal and upon the synchronizing performance. It is desirable to
limit the impulse noise to a level no greater than that of the synchronizing signal peaks so
that the operating bias of the video amplifier or the synchronizing signal separator is not
changed. In circuits where direct coupling is used, impulse noise generally does not
greatly affect the operating characteristics. A-c coupled circuits are usually affected con-
siderably by noise.
Diodes connected in shunt or series in the video amplifier have been used as impulse
noise limiters An example of a shunt-connected diode limiter is shown in Fig. 8. As the
-J-B
-1C
To synchronizing
signal separator
FIG. 8. Impulse Noise Limiter
20-56 TELEVISION
video amplifier is direct coupled to the picture detector, its operating conditions are not
seriously affected by the noise. The limiter diode D\ is connected in its anode circuit.
The d-c reinserter for the picture tube, and the synchronizing signal separator, are actuated
by the signal following the limiter and thus operate with increased reliability. The
limiter shown adjusts itself to the signal level and normally limits the peak of each syn-
chronizing pulse slightly. If the noise has a high duty cycle, this type of limiter will fail,
as the noise will then begin to bias the diode Di off, since resistor R\ will not be able to re-
move the added charge from C\ quickly enough. By stabilizing the potential of the anode
of DI with a bleeder, the limiter will handle noise of high duty cycle but will not adjust
itself to the signal level.
30. SOUND AMPLIFIERS
I-F CIRCUITS. The sound i-f amplifier of a television receiver must provide adequate
gain with proper selectivity characteristics for the f-m sound signals which accompany the
picture. The design features of television receiver sound i-f amplifiers depend largely
on the receiver type, whether broadcast a-m or f-m services are to share the channel, and
the amount of gain provided by the circuits which precede the point of sound i-f take-off.
Gain Requirements. The sound circuits should be capable of providing a comfortable
audio output with 30 per cent modulated sound carriers from 6 to 10 db weaker than the
threshold picture level. Where manual or automatic picture-gain-control circuits can
reduce the amplification in the overall sound channel by operating on tubes ahead of the
sound take-off point, an additional margin of sound gain is required.
With present techniques, the threshold picture level is of the order of 50 juv. An over-
all sound sensitivity of about 10 juv would therefore seem suitable for television, although
an additional 20 db might be desirable for broadcast frequency modulation.
When switched for television, receiver front-end circuits seldom develop more gain than
is lost by the modulator in converting to the intermediate frequencies. The sound i-f
sensitivity on the modulator grid is therefore about the same as the overall sound sen-
sitivity. The amount of sound-channel gain that may be provided between the modu-
lator grid and the point of sound take-off varies widely with receiver designs. Some pic-
ture i-f amplifiers can provide between 40 and 50 db of sound-channel gain in the modu-
lator and first one or two common stages. The most serious objection to this arrangement
is the conflict that results from manual or automatic picture gain control of these stages.
The output of the sound i-f usually feeds either a ratio-type f-m detector or a limiter
working into a conventional f-m detector. The minimum i-f output required depends on
the detector and/or limiter design and is usually in the range of 1 to 3 volts.
Selectance Characteristics. The sound i-f amplifier of a television receiver must be
broad enough not only to pass the sidebands of the carrier with full 25-kc deviation but
must also pass this signal when the local oscillator is detuned because of drift or inaccurate
resett ability of the tuning device. Minimum 6-db band widths between 200 and 400 Kc
are usual.
For television service, the sound-channel selectors should provide at least 20-db at-
tenuation at the picture carrier and 50 db or more against signals on adjacent channels.
This is considerably less severe than the requirements for broadcast frequency modulation
as outlined in Section 8. Where dual service is contemplated, the selectivity requirements
should be based on the broadcast freqiiency modulation, and it is then necessary to keep
the local oscillator frequency drift within the band width provided.
Sound Take-off Methods. Television receivers which pass 3.5- to 4-Mc video band
width usually require traps to provide sufficient attenuation of the sound intermediate
frequency in the picture channel. Such traps usually build up a sound i-f voltage or cur-
rent, and they may be coupled either directly or through additional circuit elements into
the grid of the first sound i-f amplifier. This method is applicable to simple coupled traps,
to cathode traps, and to coil arrangements in stages coupled by filter circuits.
Receivers passing less video band width may not require sound traps. The sound take-
off may then be from the secondary of a transformer whose primary is connected in series
with a picture i-f transformer; or the sound and picture i-f amplifier grids may be operated
in parallel.
Amplifier Design. There is usually negligible selectivity for the sound intermediate
frequency in the common picture and sound circuits. Some selectivity may be designed
into the take-off circuits. WTaen its gain and selectivity requirements have been estab-
lished, the sound i-f amplifier can be designed by the techniques described in Section 7.
An adequate number of single- or double-tuned circuits can give acceptable performance
provided that 20 to 30 wi over stray capacitance is added to each circuit. The align-
ment procedure will be simplified if the circuits are under-optimum coupled.
SYNCHRONIZATION 20-57
The mistiming of gain-controlled stages should be minimized either by means of unby-
passed cathode resistors or by tapping down the grid.
SOUND DETECTOR AND ATJDIO AMPLIFIER. The design of the sound detector
and the audio ^ amplifier for a television receiver follows broadcast f-m practice as dis-
cussed in Section 8. Since 100 per cent modulation on a television sound carrier cor-
responds to 25 instead of 75 Kc deviation as in broadcast frequency modulation, only one-
third the output voltage is obtained from equivalent f-m detectors. In addition, the out-
put performance of f-m detectors is usually degraded when the carrier frequency is in-
creased, as in television sound i-f amplifiers. The gain deficiency can sometimes be made
up by employing high-gain audio amplifier circuits, although this is usually undesirable,
as hum-pickup difficulties are inevitable.
An undistorted electrical output of 1 watt is probably adequate for many home tele-
vision receivers, as the audience is close to the receiver. Television receivers incorporating
broadcast f-m or a-m are usually capable of providing greater power output.
Since the current drawn by an output audio amplifier varies with the signal, and since
this current may represent a sizable fraction of the total B current drain, special considera-
tion must be given when video circuits obtain power from the same B supply. Either
adequate decoupling arrangements must be made or a constant current output amplifier
circuit must be used.
31. SYNCHRONIZATION
Adequate synchronizing circuits are among the most important features that a tele-
vision receiver must possess. The least expensive receiver must be capable of synchro-
nizing on any signal of reasonable strength without readjustment of the speed controls.
More expensive receivers may be expected to maintain synchronization on threshold weak
signals in the presence of interference.
The procedure for effecting synchronization in the television receiver consists, first, of
extracting the synchronizing pulses from the complete video wave. The line and field
pulses are then usually separated from each other and the resulting signals are used to
synchronize the respective scanning oscillators. See article 10 for a discussion of this.
SEPARATION OF SYNCHRONIZING PFLSES. One method for extracting the
synchronizing information is to provide a separate diode detector for this purpose. The
diode load resistor is by-passed by a capacitor proportioned so that the d-c voltage de-
veloped across the load resistor cannot drop more than about 20 per cent during a line
interval. The charging current in the capacitor is then a measure of signals in excess of
80 per cent of the peak amplitude of the carrier. A voltage proportional to the charging
current may be obtained across a small resistor in series with the capacitor.
This type of separator exaggerates amplitude modulation of the synchronizing signal
pulses which may be present in the complete signal. Additional amplification and limiting
are usually required.
As full video band width is not required for the synchronizing pulses, the separate de-
tector can be preceded by a high-gain narrow-band-width stage. If sufficient signal is
developed, voltage across the entire diode load, which is proportional to peak carrier am-
plitude, may be used for automatic gain control as described in article 28.
Video Separation. Synchronizing signals can be separated from a composite picture
signal by the use of limiter circuits operated in conjunction with suitable d-c stabilization
of the wave applied to the limiter. The most frequently used limiter of this type employs
a sharp cutoff tube, usually a pentode, with the signal applied to the grid with black pos-
itive (reference 70). The tube is usually operated with a grid leak and blocking con-
denser input circuit, and without bias. Grid current is, therefore, drawn on the tips of the
synchronizing pulses. The cutoff characteristic of the tube and the amplitude of the
applied video wave are correlated so that the grid swing due to the synchronizing pulses
alone exceeds the cutoff.
The self-bias d-c restoring method described above results in poor performance in the
presence of impulse-type noise unless preceded by a suitable noise limiter. A strong noise
pulse reaching the grid draws current and depresses the grid wave until the blocking ca-
pacitor can discharge. Several synchronizing pulses can thus be lost.
The synchronizing information may be extracted from picture signals of either polarity
by diode circuits, examples of which are shown in Fig. 9. The time constant of Ri and C
is proportioned so that the voltage across R\ drops to about 80 per cent during a line
interval. The diode then conducts only during the synchronizing pulse. A voltage cor-
responding to the diode's conduction is obtained across the proportionately smaller re-
sistor R2 in series with the diode.
The amplitude of the output synchronizing wave from diode separators of this type
20-58
TELEVISION
varies with picture content and usually requires amplifying and limiting for good syn-
chronization. The interelectrode capacitance of the diode may couple high video-fre-
quency component current into resistor #2.
^-Output
•^-Output
Output
_TL
FIG. 9. Diode Synchronizing Separator
SEPARATION OF LINE SYNCHRONIZING PULSES. The line synchronizing pulses
are usually separated from the complete synchronizing signal by differentiation. A
typical differentiating circuit is shown in Fig. 13, p. 20-13. This operation produces a wave
containing a series of narrow pulses coincident with the leading edges of the equalizing
pulses, the line synchronizing pulses, and the broad field synchronizing pulses, as shown
in Fig. 12, p. 20-12, to assure continuous operation of the line scan oscillator throughout
the field retrace interval.
SEPARATION OF FIELD SYNCHRONIZING PULSES. Field synchronizing pulses
can be separated from the complete synchronizing signal by integration. To preserve
reasonable rise time of the output pulses and still eliminate the line pulses, a multistage
integrator is sometimes used. An example is shown in Fig. 13, p. 20-13.
OSCILLATOR SYNCHRONIZATION. Triggering. When the triggering technique is
used, the oscillators employed are usually types that free-run at slower than the correct
speed and the synchronizing pulses are applied to initiate the retrace. The oscillators
should be designed to be insensitive to triggering except towards the end of the trace so
that the possible mistiming is limited to the interval between the oscillator's sensitivity
to triggering and its self-retrace. Multivibrators, blocking oscillators, and thyratron
oscillators are commonly used. Where oscillator voltage appears on the triggering ter-
minal, buffers are usually required.
Good performance is obtained from triggered oscillator circuits only when the syn-
chronizing waves are clean. Video components and other extraneous signals should be
small. The effects of random noise can be minimized by restricting the passband into the
SCANNING
20-59
synchronizing circuits. Impulse noise should neither greatly exceed in amplitude, nor
cause a loss of, the synchronizing pulses after the disturbance.
Phase Control. Phase-controlled scanning circuits employ oscillators whose frequency
can be controlled by a d-c voltage (reference 17) . Scanning oscillators can usually be so
controlled through the use of a d-c amplifier or a control tube. The control voltage is
obtained by measuring the phase difference between the synchronizing signal and a signal
from the scanning oscillator.
The advantage in phase-controlled synchronizing is that an extremely narrow passband
can be employed in the coupling between the phase comparison circuit and the oscillator
control point to make the oscillator insensitive to instantaneous aberrations of the syn-
chronizing wave. Random noise, impulse noise, and, usually, small amounts of video can
be tolerated. The use of a sufficiently narrow passband to achieve the desired degree of
stability tends to result in a sluggish pull-in characteristic. Typical performance is to re-
quire a second or more to lock.
32. SCANNING
Conventional scanning circuits for television receivers usually employ scanning oscil-
lators and output amplifiers. The oscillator output pulses are shaped as required and ap-
plied to the grids of output amplifiers (reference 71) to produce voltage or current waves
of proper magnitude and shape.
To achieve economies, the functions of the oscillator, wave shaper, and output amplifier
are sometimes integrated, as in the circuits shown in Figs. 9 and 11 of pp. 20-9 and 20-11.
SAWTOOTH WAVE-SHAPING CIRCUITS. The voltage wave required on the grid
of scanning output amplifiers departs from being of sawtooth form only by what is re-
quired to correct for the deficiencies in the output circuit. The usual method in scanning
generators is to integrate current pulses in a capacitor.
A typical sawtooth generator is shown in Fig. 10. The tube is normally cutoff. When
a positive pulse is applied to its grid, the capacitor in its plate circuit is discharged. Fol-
B|4-
Input
- C
• Output
4=c
Input wave
Output wave
FIG. 10. Sawtooth Wave Generator
lowing the pulse, the capacitor recharges to the supply voltage as shown at A. By using
a time constant 5 or 10 times as long as the interval between pulses, a reasonably linear
sawtooth wave may be obtained.
20-60
TELEVISION
SCANNING OSCILLATORS. Blocking Oscillators (reference 72). The blocking os-
cillator has been the preferred scanning oscillator in television receivers. A blocking os-
cillator is shown in Fig. 11. When the transformer windings are connected so that the
grid goes positive when the plate goes negative, this circuit will start oscillation and will
generate a pulse. During the pulse, grid current flows and charges the capacitor C neg-
atively, eventually terminating the pulse. The capacitor then discharges through the
resistor R to initiate a new cycle. The free-running speed is controlled by the capacitor-
the resistor, and the voltage BI.
Plate
voltage
Synchronizing
FIG. 11. Blocking Oscillator
The blocking oscillator may be synchronized by applying pulses to initiate conduction
in advance of the capacitor discharge. For phase-controlled scanning circuits, the speed
of the blocking oscillator can be regulated by controlling the voltage BI.
Multivibrators. Multivibrators are frequently used in low-priced receivers for econ-
omy. These circuits are generally regarded as being less stable, unless considerably more
than the minimum number of essential parts are employed.
A multivibrator circuit arrangement useful for television receivers is shown in Fig. 12.
The operation of this multivibrator is shown by the wave forms.
Since the current in tube B consists of a recurrent pulse wave, a wave-shaping circuit
as described in Fig. 10 may be placed in the plate circuit of this tube for generating a saw-
tooth voltage wave, as shown in Fig. 12.
Thyratron Oscillators. Thyratron tubes filled with the lighter inert gases can be used
as television scanning oscillators. The tubes are connected to discharge a capacitor in the
plate circuit. Speed is controlled by varying either the recharge time constant or by the
cathode bias. Synchronizing pulses can be applied to the grid.
The advantage of the thyratron tube lies in its ability to pass peak currents of high
SCANNING
20-61
amplitude, but time delay circuits may be required to prevent application of anode voltage
before the cathode has reached proper operating temperature.
OUTPUT AMPLIFIERS FOR ELECTROSTATIC DEFLECTION. The resolving
capabilities of most electrostatic receiver tube types can be realized only when the average
of the voltages on the deflecting plates of a pair is maintained equal to the second anode
voltage. This necessitates balanced deflection as well as balanced centering circuits.
The scanning output circuits for electrostatic tubes usually, therefore, produce sawtooth
waves of both polarities.
Typical output amplifier circuits employ two voltage-amplifier tubes connected to give
opposite polarity outputs. A separate phase inverter is seldom used; the second tube is
Output
Plate
voltage
tubeB
Plate
voltage
tube A
Cathode
sthode fcv
•ltaee\ h
h
Synchronizing
signal ,^"
'" \
Grid voltage J
tube B
-Gnd.
•"Cut off
potential
tube B
FIG. 12. Multivibrator Scanning Oscillator and Wave Shaper
usually driven by the first, either by the plate connection shown in Fig. 8, p. 20-9, or
through the common cathode resistor. Where the total scanning voltage required ex-
ceeds the order of 600 volts, the B voltage required for the output amplifier tends to be-
come quite high.
OUTPUT AMPLIFIERS, MAGNETIC. Since most magnetic scanning circuits operate
by generating and dissipating energy during each scan, the total power and the circuits
for line scanning are considerably different from those of field.
Linear magnetic deflection is accomplished by passing a sawtooth current through the
windings of the deflection yoke. The internal resistance of the amplifier, non-linearity of
the amplifier, and impedances in shunt or in series with the yoke usually require a wave
form other than sawtooth at the amplifier grid. The grid wave is thus sometimes ex-
ponential and has a pulse component added by inserting a resistor in series with the ca-
pacitor in Fig. 10.
Line (reference 82) , The usual receiver line scan circuit employs the idealized scanning
cycle shown in Fig. 10, p. 20-10. Where high efficiency is required, the triode dissipating
circuit shown in Fig. 11, p. 20-11, is used either with or without the "bootstrap" connection
which reclaims some of the scanning energy.
20-62 TELEVISION
Diode circuits are shown in Fig. 13. A high-perveance diode may be connected across
the yoke as shown in A. Lower-perveance diodes, having adequate voltage rating, may
be connected across the primary as shown in B.
Yoke
Yoke
FIG. 13.
B +
Diode Damping Circuits
Field. The output load on the field amplifier is essentially resistive so that the con-
trolled dissipation circuits used in line scanning are seldom employed. Occasionally,
damping elements are placed across the yoke to remove transients after the retrace. A
typical field scanning circuit is shown in Fig. 14.
FIG. 14. Field Scanning Circuit
33. POWER SUPPLY
The successful performance of a receiver is largely dependent on its power-supply char-
acteristics. When costs are important, the problems of power supply are among the most
difficult which the receiver designer must face.
HEATERS. Coupling. Undesired coupling in the r-f or i-f amplifiers through the
heater wiring can be minimized by grounding one side of the heaters. It is usually neces-
sary to provide appropriate by-passing of the heater lead and to interpose occasional r-f
chokes.
Heater-cathode Potentials. Except for a few types, most receiving tubes have maxi-
mum heater-to-cathode potential ratings in the neighborhood of 100 volts. Since some
POWER SUPPLY 20-63
television circuits employ tubes with cathodes at potentials relative to ground in excess of
this rating, it is necessary to provide additional windings on the power transformer when
these circuits are used. Where the off-ground cathode is at a-c ground potential, it is
customary to connect one side of the heater winding or the center tap to the cathode. If
the cathode is not at a-c ground potential, the separate winding may be connected either
to the cathode through a high resistor or to a bleeder whose voltage approximates the
operating potential of the cathode.
LOW-VOLTAGE B SUPPLY. The two major problems associated with the low-voltage
B supply for a television receiver are power-frequency ripple and cross coupling.
Power-frequency Ripple. The entrance of the power-line frequency disturbance in a
television picture may cause horizontal bands of light and dark areas, narrowing, widening,
and lateral or vertical displacement of parts of the picture, and defocusing. These effects
may be caused by the deflection of the cathode-ray-tube beam by the magnetic field of the
power transformer, or by insufficient power-frequency filtering in the power supply.
When a receiver is operated from a power line which is non-synchronous with the field
scanning, the "hum" pattern drifts upwards or downwards and is very objectionable. It
appears essential that commercial receivers be so designed that reception under these con-
ditions remains unimpaired, since programs are even now being relayed over several hun-
dred miles.
As the frequency of the power line at the receiver departs from synchronism with the
field scanning, the slowly drifting "hum" pattern jitters and flickers. This is most ob-
jectionable in even the slightest amounts. For this reason, "hum" disturbance in receivers
intended for operation from power sources whose frequencies are not synchronous with the
field scanning must not exceed about 2 per cent.
The technique for securing adequate hum filtering is to provide inductance-capacitance
filters in high-current supplies and resistance-capacitance niters in low-current supplies.
Magnetic coupling into the picture tube is most easily cured by placing the power supply
at a sufficient distance. When this is impractical, shields of high-permeability material
are placed about the tube.
Cross Coupling. Unless precautions are taken, the B supply of a television receiver
can be a troublesome source of undesired coupling between the various circuits. Tubes
taking high peak currents modulate the B supply, which may disturb circuits that handle
low-level signals. To minimize this trouble, multiple power supplies, large filter output
capacitors, such as 50 to 100 /if, multisection filters, and separate filters for susceptible
circuits are used.
HIGH-VOLTAGE SUPPLIES. The television receiver high-voltage supply provides
the power required by the second anode, and, in some cases, the focus electrode, of the
cathode-ray tube. The common types rectify power-line frequency voltage, a separately
generated sine-wave voltage, or the voltage surge present during the retrace of the line-
scanning oscillator. The voltages required range from 2 Kv for small direct-viewed tubes
to 30 Kv for projection tubes. The useful current drain from a high-voltage supply may
vary between a few microamperes with a dark screen to about 1 ma for a bright picture.
Reasonably good voltage regulation is required over the black-to-white current range if
noticeable change in picture size and defocusing is to be avoided.
To operate successfully over a number of years, the high-voltage power supply must be
designed to withstand the voltage it generates. The spacing around parts at the high po-
tential must be sufficient to prevent sparkover and the formation of corona under unfavor-
able atmospheric conditions. Insulating materials should be non-carbonizing so that they
are not damaged by a single flashover and do not become semi-conducting after periods of
service. Insulating paths should be sufficiently long to prevent excessive leakage under
conditions of dust and high humidity. Where organic materials must be used, as in a
power transformer or paper capacitor, long life can be assured only if these components
are impregnated with a good dielectric fluid and are hermetically sealed.
Power-line Frequency Supplies. This type is commonly used where the high voltage
required does not exceed 4 or 5 Kv. A single section TT filter comprising two capacitors
and a resistor is used to remove the power-frequency ripple. The resistor is usually made
as large as the voltage regulation requirements will permit and the capacitors as small as
will still afford adequate filtering. The capacitors required are usually between about
0.03 and 0.1 ptf- Since considerable energy is stored in such capacitors when charged to
voltages in excess of a kilovolt, these supplies can be lethal and thus are not suitable for
home use unless adequate safety precautions are taken. These include the following:
1. Compartmenting the power supply.
2. Interlocks to prevent access to the power-supply compartment when the power is on.
3. Bleeders capable of discharging the high-voltage capacitors to a safe voltage within
a second or less.
20-64 TELEVISION
4. A substantial connection between the receiver chassis and ground.
Locally Generated Sine-wave Supplies (references 73 and 83). This type is frequently
jsed either where no a-c power line is available or where, for the higher voltages, the cost
:>f the transformer, capacitors, and safety features of a power-line frequency supply are
excessive. It comprises a sine-wave oscillator usually operating in the low r-f range, a
step-up winding, and one or more vacuum rectifiers in either half-wave or voltage multi-
plying circuits. The rectifier filaments are customarily powered from the oscillator by
windings on the step-up transformer. Adequate filtering is usually obtained with a TT
filter comprising two capacitors and a resistor, but the capacitors are only a few hundred
micromicrofarads. When the energy storage in the capacitors is kept low, this type of
supply can be safe even though exposed and usually requires only sufficient shielding to
prevent interference by the locally generated wave.
Voltage Surge Supplies (IT. S. Patent 2,051,372). This type of power supply rectifies
the voltage surge across an inductor when the magnetic field surrounding the inductor is
suddenly changed.
The voltage surge type of supply is used in some receivers employing a magnetically de-
flected picture tube. A high-voltage winding on the line scan output transformer yields
the required voltage surge during the scanning retrace. This is rectified and filtered, and
the resultant voltage is applied to the second anode of the picture tube. It is necessary to
supply added scanning power when the second anode power is thus extracted.
Picture width, when using a high-voltage supply as described above, is adjusted by
changing the current through the yoke while not disturbing the currents in the trans-
former. Otherwise the scanning power and the second anode potential vary together and
no significant change in picture width results.
OTHER FORMS OF TELEVISION
By A. V. Loughren
The material of articles 2-33 relates primarily to monochrome, monocular television of
sharpness acceptable for home entertainment, for use with power-supply systems of 60-
cycle frequency. A change in any of these requirements may affect significantly the de-
sign of the entire television system. The more important examples of such changed re-
quirements include: (a) television standards of foreign countries; (6) theater television;
(c) color television; (d) binocular or stereoscopic television; (e) television for special uses
(e.g., military, industrial); and (/) use of a common transmitter carrier for picture and
sound modulations.
34, TELEVISION STANDARDS OF FOREIGN COUNTRIES
With respect to power-supply frequency, the practices of the several countries dif-
fer. In addition, since there has been no attempt at international standardization, in-
cidental and unnecessary differences in standards exist. Tbe standards used by the
British Broadcasting Corporation (adopted in 1937 and reaffirmed in 1944) illustrate both
points. They include:
(a) Picture repetition rate: 25 cycles per second (standard power-supply frequency is
50 cycles).
(6) Lines per frame: 405.
(c) Polarity of picture modulation: positive.
(d) Form of picture modulation : amplitude, double side band.
(e) Sound modulation: amplitude.
(/) Sound carrier location: 3.5 Me below the picture carrier frequency.
Comparison may be made with the American standards, tabulated in article 10. In
most other respects, BBC standards do not differ significantly from those of the United
States (references 74 and 75) .
35. THEATER TELEVISION
Requirements for theater television differ from those for home television primarily in
the following respects:
Highlight Brightness. Motion-picture practice provides highlight brightnesses of 2
to 20 ft-lamberts; the house is dimmed sufficiently to make this acceptable.
COLOR TELEVISION 20-65
Resolution. Pictures projected from 35-mm film have resolution considerably exceeding
that of television with a 4-Mc band width. There is some doubt that this factor out-
weighs the practical advantage of common standards, especially in view of Fig. 1 of
article 1.
Operator. Availability of a trained operator.
Picture Size. Motion-picture screens range up to 20 ft in width.
Source of Picture. Provision will probably be required for displaying pictures whether
originally picked up for broadcasting or picked up specifically for a chain of theaters. This
indicates the desirability of the common standards referred to previously.
36. COLOR TELEVISION
For reasonably faithful reproduction of colored subjects, each geometrical picture ele-
ment must be represented not by a single intensity, its brightness (as required for mono-
chrome television) , but by three separate quantities. These may be the brightnesses of
three "primary" colors. Alternatively, one signal may represent the resultant hue, a
second the saturation of that hue, and the third, the brightness. Color measurement
and specification may be done by either of these alternatives.
Color reproduction systems are divided into additive and subtract ive systems. In an
additive system, for each picture element an individual stream of light energy in each of
the primary colors reaches the eye of the observer. If the light as originally generated is
white, a major portion of it is discarded in the filters, which transform it to light of the
primary colors. In a subtractive system, the originally produced white light is modified
individually for each picture element by subtracting only the unwanted color components.
The subtractive system consequently shows an efficiency in the use of a white-light source
which is several times that of an additive system. In color photography, subtractive
processes such as Technicolor and Kodachrome have found much greater acceptance than
the additive processes such as Autochrome and Finlay. In color television, on the other
hand, only systems of the additive type have been developed sufficiently to promise prac-
tical utility.
For additive systems, desirable reproduction primaries are red, green, and blue, in-
dividually chosen as compromises between purity (or saturation to increase the range of
producible colors) and transmission loss from white light. Colors equivalent to the trans-
missions through Wratten filters numbers 47, 58, and 25, when the light source is the
International Committee on Illumination's Illuminant "C," have found some acceptance
as the red, green, and blue primaries.
METHODS OF TRANSMISSION. Numerous methods of transmission of color
television signals have been proposed. Of the several ways of classifying these methods
a classification by the time characteristics of the signal seems most important. On this
basis, the systems may be classified as:
1. Simultaneous systems, in which the three elements of information required to
describe a single picture element are transmitted simultaneously.
2. Sequential systems, in which the three elements of information are transmitted
successively. The sequential systems which have been proposed fall into the following
subclasses:
(a) Field Sequential. A complete picture field is transmitted in one color, followed by
successive fields in the remaining colors. In a three-color system with 2 : 1 interlace, six
fields must elapse before a picture which is complete both geometrically and in color may
be obtained.
(&) Line Sequential. A line of one color is transmitted, followed by successive lines in
the remaining colors, and the cycle repeats. In this system if the number of colors is an
integral submultiple of the number of lines in a complete picture, a given picture line
(for example, the eleventh) will always be repeated in the same color unless the color se-
quence switching is momentarily altered at the end of a frame to produce a new phasing
for the next frame. With three colors it is difficult to avoid in a line sequential system a
"crawling" tendency in the produced image which has usually been exhibited in systems
with orders of interlace greater than 2:1,
(c) Dot Sequential. The three bits of information describing an individual picture ele-
ment are transmitted in immediate succession, after which transmission of information
for the next picture element takes place. In this system a dot pattern somewhat similar
to that of a halftone engraving appears superposed on the colored portions of the picture.
It is interesting to note that dot sequential systems are closer in their characteristics to
simultaneous systems than to the other sequential systems.
Color television systems may be also classified in accordance with the quantities ex-
20-66 TELEVISION
plicitly represented by the elements of the transmitted signals. Among the many possi-
bilities are the following:
1. Intensities of individual primary colors.
2. Composite intensity (or, alternatively, visual brightness) plus two auxiliary signals
representing, for example, the difference between the apparent brightness and the red
and blue intensities respectively.
3. Composite intensity, hue, and saturation.
PHYSIOLOGICAL REQUIREMENTS. Resolution. It has been shown that, in a
color picture, the apparent resolution is not appreciably impaired when the blue image is
severely defocused; it is also known that moderate defocusing of the red image is permis-
sible. Further, the use of a common signal to represent the fine detail for all three
colors can be demonstrated as causing negligible impairment of picture quality, when
practiced in reasonable amounts.
Since brightness is largely determined by the green content of a color, it appears from
the foregoing facts that resolution may be effectively preserved, and yet the frequency
band effectively conserved, by a system of transmission in which brightness is transmitted
with a band of several megacycles, while hue and saturation are transmitted with relatively
narrow bands. If this practice is applied to a system in which separate components of
the radiated signal represent the intensities of the primary colors, the low-frequency por-
tion of each color component of the signal will be derived individually (to represent the
distribution of light of its corresponding color in the subject) while the high-frequency
portion will be identical in all three colors. This common high-frequency signal has been
called "mixed highs."
No studies comparable to that of reference 4 have been made for color pictures; in the
absence of such information, it seems probable that resolution comparable to that of mono-
chrome television is desirable, especially for the brightness component.
Flicker. The apparent brightness of a color image is determined largely by the green
component. If the entire image (or an interlaced image .field) is produced in each color,
the flicker performance is essentially that given by considering the repetition rate of the
green component only.
Color Range. The available color reproduction range of a television system using the
reproducing primaries suggested above is comparable to the best ranges obtained by
commercial color reproduction processes of other sorts such as color film and multicolor
printing. Such a range appears adequate.
COMPATIBILITY. When a color television system is put into use in an area already
provided with a monochrome television service, the question of compatability arises. A
color television system is compatible with a particular monochrome television system
when color television signals radiated by the color system may be received as monochrome
images of acceptable quality on the receivers of the monochrome system without modifi-
cation to such receivers. The possession of this characteristic by a color television system
contributes importantly to making the commercial introduction of the color system easy
since:
1. Color transmissions may be started by individual stations of the monochrome tele-
vision service as soon as the stations are equipped for color pickup, with no loss of audience
or impairment of audience satisfaction.
2. Those viewers who are immediately interested in receiving color may purchase new
color receivers with assurance that, since the audience for color broadcasts includes both
themselves and the monochrome audience, program service will develop rapidly.
For a color system to be compatible with a monochrome system it must employ essen-
tially the same transmission standards as the monochrome system. Any changes in the
standards either must be small enough in amount to be without effect on operation of the
monochrome receivers or must be in the nature of additions to the signal of a sort which
will go undetected by the monochrome receivers. Dot sequential systems, because of
their superior potentialities for band-width economy, seem more likely to be capable of
operation compatible with the present FCC monochrome standards with a satisfactory
grade of reproduced picture than the systems using slower color sequence rates.
TRANSMITTER. Color television transmitters differ necessarily from monochrome
transmitters in requiring the use of a color camera and possibly additional control signals
for color synchronizing information, etc. In other respects, however, they may be essen-
tially similar to a monochrome transmitter. The detailed requirements for the camera and
the additional control signals are dependent on the particular color television system
considered.
RECEIVER. A receiver for color television differs necessarily from a receiver for mono-
chrome television only in the substitution of a display capable of giving color reproduc-
tion and the addition of circuits to convert the output of the receiver's detector into
REFEKENCES 20-67
signals appropriate to the particular display. The circuits needed are those used to
synchronize and phase the effective color of the display to correspond to the color of the
bit of picture information being supplied to the display at the corresponding instant. If
the system is field sequential so that the color switching rate is once per field, the circuits
may control the synchronizing and phasing of a motor driving a color wheel — a disk pro-
vided with a series of sectors in the successive colors. In an all-electronic display the color
signals must perform a corresponding function; in the electronic arrangements the rate of
switching from one color to the next may be arranged to accommodate either dot sequen-
tial, line sequential, or field sequential systems.
See also references 1, 5, 25, 76, 77, 85-92.
37. BINOCULAR TELEVISION
In direct viewing of a scene, the images formed in an observer's right and left eyes dif-
fer. Depth perception is based, in part, on this difference, as discussed in Section 14.
Presentation of suitably different reproduced images to an observer's two eyes will in
many cases enhance the illusion of solidity in a reproduced picture.
Binocular^ or stereoscopic presentation to a viewer must provide that each eye sees only
the picture intended for it. Among the means used for this purpose have been (1) bar-
riers and lenses to direct each eye correctly; (2) alternate display of the right and left images
with spectacles worn by the viewer containing a synchronized mechanical shutter; (3) al-
ternate display of a red right image and a green left image, with viewer spectacles having
no green transmission to the right eye and no red transmission to the left eye; and (4) al-
ternate display of a right image with horizontally polarized light and a left image with
vertically polarized light, with complementary viewer spectacles.
For the three-dimensional illusion to be most effective, the spacing between the posi-
tions of the camera in taking the images should be equal to the average ocular separation
(unless the image is to be magnified in reproduction) . The presentation of separate pic-
tures for the two eyes requires transmission of twice the information (and, hence, twice
the band width) required for monocular presentation.
The need for special viewing devices has prevented any wide interest in binocular tele-
vision.
38. TELEVISION FOR SPECIAL SERVICES
Proposals for industrial and for military uses of television have often presented require-
ments radically different from those of television broadcasting for home entertainment.
Examples of these unusual requirements have included: (1) effective protection against
jamming; (2) secrecy; (3) severe size and weight limitations; (4) unattended transmitter
and camera operation; (5) the high importance accorded to reliability; (6) the usual rel-
atively unfavorable operating conditions (as compared to household use) encountered in
many forms of industrial and military apparatus design. Requirements of this sort may
affect basically the design of the television system, in addition to their obvious effect on the
detailed design of the apparatus. For examples of designs for military purposes, see refer-
ence 78.
39. DIPLEXING OF PICTURE AND SOUND
Use of a single carrier for both picture and sound modulations is of interest because of
possible simplification of receivers and decrease of radio spectrum space resulting from it.
Possible approaches include: (a) use of different (and mutually non-interfering) forms of
modulation for the two signals — for example, amplitude modulation for the picture, with
frequency modulation for the sound; (6) sharing of time between picture and sound signals.
Method (a) has not been tried widely, probably in view of the general use of vestigial
sideband picture transmission, with its inherent introduction of picture frequency modula-
tion sidebands representing all but the lowest frequencies and the consequent likelihood
of cross-talk between the two signals in a receiver.
Method (b) has been proposed on several occasions and has had some laboratory and
field trials. It is found that the frequency of the intervals in which sound signals are
transmitted is between two and three times the highest sound modulation frequency which
can be successfully transmitted, and that the resulting sound-signal-to-noise ratio is de-
pendent on the fraction of the total time used for sound and on the details of the sound
modulation process. The sound intervals must be so located relative to the picture sig-
nals, in time, as to produce no visible effect; they may, therefore, be placed between the
20-68 TELEVISION
synchronizing signal and the start of the picture information for each scanning line. See
reference 79 for a more complete discussion and bibliography.
REFERENCES
1. "Optics," Section 14 of this handbook.
2. Wilson, J. C., Television Engineering, Pitman (1937).
3. Engstrom, E. W., A Study of Television Image Characteristics, Proc. I.R.E., Vol. 21, No. 12,
pp. 1631-1651 (December 1933), and Vol. 23, No. 4, pp. 295-310 (April 1935).
4. Baldwin, M. W., The Subjective Sharpness of Television Images, Proc. I.R.E., Vol. 28, No. 10,
pp. 458-468 (October 1940).
5. Hardy, A. C., Handbook of Colorimetry, Technology Press (1936).
6. Mertz, P., and F. Gray, A Theory of Scanning, Bell Sys. Tech. J., Vol. 13, No. 3, pp. 464-515
(July 1934).
7. Wheeler, H. A., and A. V. Loughren, The Fine Structure of Television Images, Proc, I.R.E., Vol.
26, No. 5, pp. 540-575 (May 1938).
8. Campbell, G. A., and R. M. Foster, Fourier Integrals for Practical Applications, Bell Telephone
System Monograph B584.
9. Wheeler, H. A., The Interpretation of Amplitude and Phase Distortion in Terms of Paired Echoes,
Proc. I.R.E., Vol. 27, No. 6, pp. 359-385 (June 1939).
10. Robinson, D. M., The Supersonic Light Control, Proc. I.R.E., Vol. 27, No. 8, pp. 483-486 (August
1939).
11. Sieger, J., Television Receivers Using the Scophony Optical Scanning System, Proc, I.R.E., Vol.
27, No. 8, pp. 487-492 (August 1939).
12. Wikkenhauser, G., Synchronization of Scophony Television Receivers, Proc. I.R.E., Vol. 27,
No. 8, pp. 492-496 (August 1939).
13. Lee, H. W., Optical Design of Television Receiver Using Moving Scanners, Proc. I.R.E., Vol. 27,
No. 8, pp. 496-500 (August 1939).
14. Rosenthal, A. H., A System of Large-screen Television Reception Based on Certain Electron
Phenomena in Crystals, Proc. I.R.E., Vol. 28, No. 5, pp. 203-212 (May 1940).
15. Donal, J. S., Jr., Cathode-ray Control of Television Light Valves, Proc. I.R.E., Vol. 31, No. 5,
pp. 195-208 (May 1943).
16. Donal, J. S., Jr., and D. B. Langmuir, A Type of Light Valve for Television Reproduction, Proc.
I.R.E., Vol. 31, No. 5, pp. 208-214 (May 1943).
17. Wendt, K. R., and G. L. Fredendall, Automatic Frequency and Phase Control of Synchronization
in Television Receivers, Proc. I.R.E., Vol. 31, No. 1, pp. 7-15 (January 1943).
18. Poch, W. J., and D. W. Epstein, Partial Suppression of One Side Band in Television Reception,
Proc. I.R.E., Vol. 25, No. 1, pp. 15-31 (January 1937).
19. Hollywood, J. M., Single-Sideband Filter Theory with Television Applications, Proc. I.R.E.,
Vol. 27, No. 7, pp. 457-472 (July 1939).
20. Nergaard, L. S., A Theoretical Analysis of Single-Sideband Operation of Television Transmitters,
Proc. I.R.E., Vol. 27, No. 10, pp. 666-677 (October 1939).
Detai
21. Goldman, Stanford, Television Detail and Selective-Sideband Transmission, Proc. I.R.E., Vol. 27,
No. 11, pp. 725-732 (November 1939).
22. Kallman, H. E., and R. E. Spencer, Transient Response of Single-Sideband Systems, Proc. I.R.E.,
Vol. 28, No. 12, pp. 557-561 (December 1940).
23. Singer, C. P., A Mathematical Appendix to Transient Response of Single-Sideband Systems, Proc.
I.R.E., Vol. 28, No. 12, pp. 561-563 (December 1940).
24- Wheeler, H. A., The Solution of Unsymmetrical-Sideband Problems with the Aid of the Zero-
Frequency Carrier, Proc. I.R.E., Vol. 29, No. 8, pp. 446-458 (August 1941).
25. Goldmark, Dyer, Piore, and Hollywood, Color Television Part I, Proc. I.R.E., Vol. 30, No. 4,
pp. 162-182 (April 1942) ; Goldmark, Piore, Hollywood, Chambers, and Rives, Color Television
Part II, Proc. I.R.E., Vol. 31, No. 9, pp. 465-478 (September 1943).
26. Zworykin, V. K, The Iconoscope, Proc. I.R.E., Vol. 22, No. 1, pp. 16-32 (January 1934).
27. Bedford, A. V., and J. P. Smith, A Precision Television Synchronizing Signal Generator, RCA Rev.,
Vol. V, No. 1, pp. 51-68 (July 1940).
28. Fink, D. G. (editor), Television Standards and Practice— NT 'SC, McGraw-Hill.
29. Mertz, P., Television— The Scanning Process, Proc. I.R.E., Vol. 29, No. 10, pp. 529-537 (October
1941).
30. Rose, Weimer, and Law, The Image Orthicon — A Sensitive Television Pickup Tube. Proc. I.R.E.,
Vol. 34, No. 7, pp. 424-432 (July 1946).
31. Beers, G. L., The Focusing Viewfinder Problem in Television Cameras, Proc. I.R.E., Vol. 31, No. 3,
pp. 100-106 (March 1943).
32. Nicoll, F. H., A New Chemical Method of Reducing the Reflection of Glass, RCA Rev., Vol. 6,
No. 3, pp. 287-301 (January 1942).
33. De Vore and lams, Some Factors Affecting the Choice of Lenses for Television Cameras, Proc.
I.R.E., Vol. 28, No. 8, pp. 369-374 (August 1940).
34. Larsen and Gardner, Image Dissector, Electronics, Vol. 12, p. 24 (October 1939).
35. Monfort and Somers, Measurement of the Slope and Duration of Television Synchronizing Im-
pulses, RCA Rev., Vol. 6, No. 3, pp. 370-389 (January 1942).
36. Maloff, I. G., Gamma and Range hi Television, RCA Rev., Vol. 3, No. 4, pp. 409-417 (April 1939).
37. Bamford, H. S., A New Television Film Projector, Electronics, Vol. 11, p. 25 (July 1938.)
38. Engstrom, Beers, and Bedford, Application of Motion Picture Film to Television, RCA Rev.,
Vol. 4, No. 1, pp. 48-81 (July 1939).
39. Bedford and Fredendall, Transient Response of Multistage Video Frequency Amplifiers, Proc.
I.R.E., Vol. 27. No. 4, pp. 277-284 (April 1939).
40. Bedford and Fredendall, Analysis, Synthesis, and Evaluation of the Transient Response of Tele-
vision Apparatus, Proc. I.R.E., Vol. 30, No. 10, pp. 440-457 (October 1942).
41. Loughlm, B. D., A Phase Curve Tracer for Television, Proc. I.R.E., Vol. 29, No. 3, pp. 107-115
(March 1941).
42. Kell, Bedford, and Kozanowski, A Portable High Frequency Square Wave Oscillograph for Tele-
vision, Proc. I.R.E., Vol. 30, No. 10, pp. 458-464 (October 1942).
43. Townsend, C. L., Contemporary Problems in Television Sound, Proc. I.R.E., Vol. 31, No. 1,
pp. 3-7 (January 1943).
REFERENCES 20-69
44. Shelby and See, Field Television, RCA Rev., Vol. 7, No. 1, pp. 77-93 (March 1946).
45. fetrieby and Wentz, Television Transmission over Wire Lines, Bell Sys. Tech. J., Vol. 20, No. 1,
pp. 62-81 (January 1941).
46. Strieby and Weis, Television Transmission, Proc. J.E.S., Vol. 29, No. 7, pp. 371-381 (July 1941).
47. HanseU, C. W Radio Relay Systems, Proc. I.R.E., Vol. 33, No. 3, pp. 156-168 (March 1945).
48. Frus, H. 1 ., A Note on a Simple Transmission Formula, Proc. I.R.E., Vol. 34, No. 5, pp. 354-356
(May 1946).
49. Parker, W. N., A Unique Method of Modulation for High Fidelity Television Transmission,
Crt -o-Sf^'J'^'^ Vofe 26' No' 8' pp' 946~962 (August 1938).
50. PJHA Nordlohne, Experimental Short Wave Broadcasting Station PCJ, Phillips Tech. Rev., Vol. 3,
No. 1, pp. 17-27 (January 1938).
51. Kell and Fredendall, Selective Side Band Transmission in Television, RCA Rev., Vol. 4, No. 4,
pp. 425-440 (April 1940).
52. grown G H., A Vestigial Side Band Filter, RCA Rev., Vol. 5, No. 3, pp. 301-326 (January 1941).
53. Buzalski, T. J A Method of Measuring the Degree of Modulation of a Television Signal, RCA
Rev., Vol. 7, No. 2, pp. 265-271 (June 1946).
54. Lindenblad, N. E., Television Transmitting Antenna, RCA Rev., Vol. 3, No. 4, pp. 387-408
(April 1939).
55. Carter, P. S., Simple Television Antennas, RCA Rev., Vol. 4, No. 2, pp. 168-185 (October 1939).
56. Janes, R. B., and W. A. Hickok, Recent Developments in the Design Characteristics of the Icono-
scope, Proc. I.R.E., Vol. 27, No. 9, p. 535 (September 1939).
57. Johnson, E. O., Development of an Ultra Low Loss Transmission Line for Television, RCA Rev.,
Vol. VII, No. 2, pp. 272-280 (June 1946).
58. Herold, E. W., Local Oscillator Radiation and Its Effect on Television Picture Contrast, RCA Rev.,
Vol. VII, No. 1, pp. 32-53 (March 1946).
59. Herold, E. W., Superheterodyne Converter System Considerations in Television Receivers, RCA
Rev., Vol. IV, No. 3, pp. 324-337 (January 1940).
60. Herold, E. W., The Operation of Frequency Converters and Mixers for Superheterodyne Reception,
Proc. I.R.E., Vol. 30, No. 2, pp. 84-103 (February 1942).
61. Jones, M. C., Grounded-Grid Radio-Frequency Voltage Amplifiers, Proc. I.R.E., Vol. 32, No. 7,
pp. 423-429 (July 1944).
62. Seeley, S. W., Effect of the Receiving Antenna on Television Reception Fidelity, RCA Rev., Vol. II,
No. 4, pp. 433-441 (April 1938).
63. Herold, E. W., An Analysis of the Signal to Noise Ratio of Ultra High Frequency Receivers, RCA
Rev., Vol. VI, No. 3, pp. 302-331 (January 1942).
64. Mount joy, G., Television Signal-Frequency Circuit Considerations, RCA Rev., Vol. IV, No. 2,
pp. 204-230 (October 1939).
65. Tyson, B. F., A Preselector Circuit for Television, Electronics, Vol. 13, pp. 23-25 (November 1940).
66. Nyquist, H., Certain Topics in Telegraph Transmission Theory, Trans. A.I.E.E., Vol. 47, pp. 617-
644 (April 1928).
67. Mountjoy, G., Simplified Television IF Systems, RCA Rev.t Vol. IV, No. 3, pp. 299-309 (January
1940).
68. Freeman, R. L., The Use of Feedback to Compensate for Input-Capacitance Variations with Grid
Bias, Proc. I.R.E., Vol. 26, No. 11, pp. 1360-1366 (November 1938).
69. Wheeler, H. A., Wide-Band Amplifiers for Television, Proc. I.R.E., Vol. 27, No. 7, pp. 429-438
(July 1939).
70. Zworyldn, V. K.T and G. A. Morton, Television (a book), Chapter 15, p. 465; Chapter 17, p. 524,
Wiley (1940).
71. Puckle, 0. S., Time Bases, Chapter V, pp. 64-66, 68-69; Chapter VIII, pp. 115-122, Wiley (1943)
72. Maloff, I. G., and D. W. Epstein, Electron Optics in Television, Chapter 13, p. 255, McGraw-Hill.
73. Schade, 0. H., Radio-Frequency Operated High- Voltage Supplies for Cathode-Ray Tubes, Proc.
I.R.E., Vol. 31, No. 4, pp. 158-163 (April 1943).
74. Blumlein, A. D., The Marconi-E.M.I. Television System: Part I. The Transmitted Wave-Form,
J. I.E.E., Vol. 83, No. 504, pp. 758-766 (December 1938).
75. Report of the Television Committee, 1943, Right Hon. Lord Hankey, Chairman, His Majesty's
Stationery Office, London.
76. Judd, Deane B., Introduction to Color, from Symposium on Color, American Society for Testing
Materials, pp. 1-12.
77. Friedman, Joseph S., History of Color Photography, American Photographic Publishing Company.
78. Marshall and Katz, Television Equipment for Guided Missiles, Proc. I.R.E., Vol. 34, No. 6, pp.
375-401 (June 1946).
79. Fredendall, Schlesinger, and Schroeder, Transmission of Television Sound on the Picture Carrier,
Proc. I.R.E., Vol. 34, No. 2, pp. 49-61 (February 1946).
80. Sziklai, G. C., Current Oscillator for Television, Electronics, Vol. 19, No. 9, pp. 120-123 (September
1946) .
81. Zworykin and Morton, Television, Chapter 15, pp. 471-473, Wiley (1940). ,_.,„_
82. Friend, A. W., Television Deflection Circuits, RCA Rev., Vol. VIII, No. 1 (March 1947).
83. Mautner, R. S., and O. H. Schade, Television High Voltage R-F Supplies, RCA Rev., Vol. VIII,
84. Wendt, K. R., The Television D-C Component, RCA Rev., Vol. 9, No. 1, pp. 85-111 (March 1948).
85. Evans, Ralph M., An Introduction to Color, Wiley (1948). ^,, T,T,T>_TTi,^.
86. An Experimental Simultaneous Color-Television System: Kell, R. D., Part I, Introduction ;
Sziklai, G. C., Ballard, R. C., and Schroeder, A. C., Part II, Pickup Equipment; Wendt, K. R.,
Fredendall G. L. and Schroeder, A. C., Part III, Radio Frequency and Reproducing Equip-
ment; Proc. I.R.E., Vol. 35, No. 9, pp. 861-875 (September 1947) .
87. Battison, John H., Color Television Transmission Systems, Tele-Tech, Vol. 8, No. 10, pp. 18-20
88. Report° of ^CC Color TV Demonstrations at Washington, Tele-Tech, Vol. 8, No. 11, pp. 24-26
89. Loomil,6 Franklin, Highlights of FCC Color-TV Demonstrations, Tele-Tech, Vol. 8, No. 12, pp.
90. New'DirectfonSVcolor Television, Electronics, Vol. 22, No. 12, pp. 66-72 (December 1949).
91. Boothroyd, Wilson, Dot Systems of Color Television, Part I, Electronics Vol. 22, No. 12, pp.
88-92 ^December 1949); Part II, Electronics, Vol. 23 Np..l, pp 96-99 January 1950).
92 RCA Laboratories, A Six-Megacycle Compatible High-Definition Color Television System, RCA
Rev., Vol. 10, No. 4, pp. 504-524 (December 1949).
SECTION 21
ELECTRONIC CONTROL EQUIPMENT
BY
B. J. DALTON
FUNDAMENTAL ELECTRONIC POWER
ART. CIRCUITS PAQB
1. Rectifier Circuits and Applications 03
2. Non-controlled Rectifiers 08
3. Controlled Rectifiers and Inverters 09
4. Thyratron and Ignitron Contactors, ... 11
FUNDAMENTAL ELECTRONIC CONTROL
CIRCUITS
5. Stabilized D-c Control Power Supplies. . 14
6. Timing Circuits 14
7. D-c Amplifiers 16
ART. PAGE
8. A-c Amplifiers 16
9. Regulating Circuits 17
10. Tliyratron Grid-control Circuits 19
COMPLETE ELECTRONIC DEVICES
11. Electronic Relays 20
12. Resistance-welder Controls 23
13. D-c Motor Control 27
14. Side-register Positioning Control 30
15. Process Controls 32
16. System Stabilisation 32
21-01
ELECTRONIC CONTROL EQUIPMENT
By B. J. Dalton
FUNDAMENTAL ELECTRONIC POWER CIRCUITS
The fundamental purpose of any electronic rectifier is to convert alternating current
into direct current. Therefore, it can be considered as a d-c power supply, the same as a
battery or a motor-generator set. There are, however, two important differences between
rectifiers and generators or batteries:
1. Batteries supply a smooth d-c voltage output; generators have a number of com-
mutator segments so that the instantaneous voltage at the brushes is nearly constant;
rectifiers, on the other hand, generally consist of a relatively small number of phases and
rectifying elements and therefore almost all of them have a considerable amount of ripple
voltage in the output. The ripple voltage must be considered in many applications, and
in particular those involving less than 6-phase rectification, because the ripple voltage
may produce a current ripple in some loads which will cause excessive heating not only
in the load but also in the rectifier transformer and the rectifying elements. A highly
inductive load is a very desirable rectifier load, because the inductance smooths out most
of the current ripple. Resistance loads and particularly counter emf or capacitive loads
will result in high rms currents which cause additional heating. 'In some counter-emf
type loads it may be desirable to include sufficient reactance in the rectifier output circuit
to limit the peak current to a reasonable value. This obviates the necessity for excessive
rectifying element and transformer sizes and also minimizes the additional heating which
would otherwise be present in the load.
2. Batteries are inherently energy-storage devices and have a constant output voltage;
generators not only have a small amount of energy stored mechanically in their rotor
but also are usually driven by an a-c motor the speed of which is reasonably independent
of a-c line voltage; thus the generator has a constant output voltage. Rectifiers, on the
other hand, have no inherent energy storage, and the output voltage at any instant is
directly proportional to the a-c input voltage. Therefore, if a constant d-c output voltage
is desirable, either the a-c input voltage must be regulated or a regulating means must be
provided for the output voltage.
The efficiency of electronic rectifiers is determined by the losses in the rectifying ele-
ments themselves together with transformer losses, cathode heating losses, and miscel-
laneous auxiliary losses. The power factor of a rectifier is determined by the type of
load and number of phases and for a controlled rectifier by the amount of phase retard as
well. An inductive load will give the highest power factor; a counter-emf load will result
in the lowest power factor. For a given type of load, the power factor is inversely propor-
tional to the amount of phase retard, the rectifier being essentially a constant-kva load
on the power line.
One or more of the following factors will govern the choice of the type of rectifier for a
specific application:
1. The magnitude of the required d-c power.
2. The magnitude of the required d-c voltage.
3. The magnitude of the required d-c current.
4. The required degree of freedom from a-c voltage ripple in the d-c output voltage or
current.
5. The effect of the connected load on the rectifying elements.
6. "The number of phases and the type of connection available from the a-c power supply.
7. The magnitude of the a-c power supply voltage.
8. The necessity for adjusting the output voltage.
9. The necessity for regulating the output voltage at a specific value.
10. Physical size.
11. Cost.
Electronic rectifiers may be classified in accordance with their controllability as (1) non-
controlled, (2) grid-controlled, and (3) ignitron or pool-type-controlled rectifiers. (These
types will be discussed in greater detail later.) Also electronic rectifiers may be classified
in accordance with the type of circuit connection used.
21-02
RECTIFIER CIRCUITS AND APPLICATIONS 21-03
The proposed AIEE standards for pool-cathode mercury-arc power converters include
a list of 36 standard rectifier circuit connections. Table I, however, illustrates eight circuit
connections which are representative of a large number of applications, and in particular
those applications in the low- and medium-power field. These circuits and their uses are
described below.
1. RECTIFIER CIRCUITS AND APPLICATIONS
Half-wave rectifiers are generally limited in their application to low power circuits.
Typical half-wave rectifier applications are: (1) D-c power supplies for small electronic
amplifiers. In this application a filter circuit is used to store energy during the half cycle
in which the rectifier element is conducting so that a reasonably smooth output voltage
can be obtained. ^(2) D-c power for operating d-c coils of magnetic relays. (3) Charging
circuits for capacitors. (4) D-c power supplies for the armature power for small d-c
motors. (5) Battery charging equipment. Half-wave rectifiers are generally used because
of their simplicity and relatively low cost. Furthermore the half-wave rectifier circuit
can be operated directly from a single-phase power supply, without an anode transformer,
if the load is designed to match the obtainable output voltage. The half-wave circuit,
however, is undesirable in some respects because the energy delivered to the load in an
entire cycle must be obtained during one-half cycle. This reduces the transformer utiliza-
tion (if a transformer is used) and also results in high peak currents in the rectifying ele-
ment. In addition, this type of rectifier is generally unsuited for application to highly
inductive (i.e., iron-core inductance) loads. The time constant of an inductive load is
usually sufficiently long so that current will not build up during the half cycle in which
the tube can conduct. The small amount of energy that is transferred into the load is
inverted during the non-conducting half cycle. Usually the average current is about 10
to 20 per cent of that which would be expected in a pure resistance. A capacitor or a
rectifier tube is sometimes connected across an inductive load to prevent the energy stored
in the inductance from being transferred to the a-c supply during the normally non-
conducting half cycle. Thus the current can build up over a period of time and finally
reach a steady-state value.
The diametric (full-wave) rectifier is used in a large number of low-power applications.
Typical applications are: (1) d-c power supplies for other electronic equipment; (2) d-c
power supplies for magnetic clutches, magnetic chucks, and lifting magnets; (3) battery
chargers; (4) d-c power for supplying the fields of d-c motors and generators; (5) d-c power
for the armature circuit of d-c motors. This rectifier is a relatively simple and inexpensive
unit. In some applications, however, its usefulness is limited by the amount of ripple
present in the output voltage. The desirability of obtaining larger amounts of power from
polyphase power supplies usually limits its use to applications involving less than 5 kw
of d-c power.
The primary advantage of the diametric, double-way (bridge) rectifier is its ability to
supply high voltages. The peak inverse voltage across the rectifying element is only half
of what it would be in a diametric (full-wave) circuit. Thus a diametric, double-way
rectifier can be designed to deliver twice the d-c voltage that a diametric rectifier can
deliver, assuming the same rectifying elements in both cases. It also results in high trans-
former utilization. This rectifier circuit has another advantage in that it can be operated
directly from a single-phase power supply without an anode transformer, provided that
the output voltage obtained this way is of a suitable value.
Polyphase rectifiers are generally used whenever large amounts of power are required.
The selection of a particular polyphase rectifier is largely a matter of obtaining the desired
output voltage and current from existing or standard rectifying elements. For example,
if rectifying elements of 5-amp capacity each were available and a 15-amp d-c output were
required, a delta 3-phase wye rectifier circuit could be chosen. Likewise if 20 amp of
direct current were required using the same rectifying elements, a Scott 4^phase cross
rectifier circuit could be selected. A delta 6-phase star rectifier circuit could be selected
to obtain 30 amp of direct current from the same rectifying elements. However, it might
be that the use of such a circuit as the delta 6-phase star would place a severe duty on a
particular rectifying element either from the standpoint of the rms current or from the
standpoint of the peak current. For example, if an excessive peak or rms rectifier current
would exist in a delta 6-phase star circuit, the delta 6-phase double-wye circuit could be
chosen. This would reduce the rms and peak currents by a ratio of almost 2 to 1. It is
sometimes possible by careful coordination of power supply connections and load voltage
ratings to use a delta 6-phase wye double-way rectifier to eliminate the rectifier trans-
former. Double-way rectifiers, as mentioned before, will deliver higher d-c voltages, for a
given peak inverse voltage across the rectifying elements, than single-way rectifiers.
21-04
ELECTRONIC CONTROL EQUIPMENT-
RECTIFIER CIRCUITS AND APPLICATIONS
21-05
I
£
i
1
T
<H
1
.2 <u
tl
21-06
ELECTBONIC CONTROL EQUIPMENT
31
H
Tube Cur
Wave F
esistance
1
JL
T
T"
-53 a
Q
RECTIFIER CIRCUITS AND APPLICATIONS
21-07
"3
X
T3
X
1
«
H
2
PH
21-08 ELECTRONIC CONTKOL EQUIPMENT
Sometimes the requirement of low ripple currents governs the choice of the rectifier circuit,
rather than the current capacity. For very large rectifiers above 1000 kw (total installed
capacity) , 12 or more phase rectifiers may be used to minimize the effect of rectifier har-
monics on telephone lines.
EXPLANATION OF TABLE 1. Table 1 consists of four distinct sections appearing
from left to right as follows: (1) circuit nomenclature and connection diagrams; (2) output
voltage wave shapes, required transformer-secondary voltage ratings, and output-voltage
ripple values; (3) rectifying element current wave shapes (for resistance load), rectifying-
element current values (for resistance load), and rectifying-element peak inverse voltages;
(4) rectifier-transformer kva ratings, for both resistive and inductive loads. All data are
tabulated in terms of the theoretical no load d-c output voltage (Edo) and output cur-
rent (Id).
The usefulness of this table can best be illustrated by means of an example.
Problem. To specify (a) the transformer-secondary voltage rating; (6) the transformer-
secondary and primary kva ratings; (c) the average, rms, and peak current which the
rectifying elements will need to carry; and (d) the peak inverse voltage which will exist
across the rectifying elements, for a diametric (full-wave) rectifier to deliver 10 amp of
direct current at 250 volts. Assume that there is no voltage drop in the rectifying ele-
ments; also assume a resistance load.
Solution: (a) Transformer-secondary voltage each side of center tap = 1.11 X 25QEdo
= 277.5 volts
Total secondary volts = 555.0
(6) Transformer secondary kva rating = 1.75 X d-c, kw
_ 1.75 X 10 amp X 250 volts
1000
= 4.37 kva
Transformer-primary kva rating = 1.235 X d-c kw
_ 1.235 X 10 X 250
1000
= 3.09 kva
(c) Rectifying-element currents
Average = 0.5 X 107<j = 5 amp
Rms = 0.786 X 10/d = 7.86 amp
Peak = 1.57 X 101* = 15.7 amp
(d) Rectifying-element peak inverse voltage = 3.14 X 250^do = 785 volts. (The
actual ratings will need to be increased to compensate for the voltage drop in the rectifying
elements, transformer reactance, and the like.)
2. NON-CONTROLLED RECTIFIERS
The types of non-controlled electronic rectifying devices in common use are: (1) high-
vacuum tubes; (2) hot-cathode gaseous rectifier tubes; (3) metallic rectifiers.
Non-controlled rectifiers are used in applications where a fixed amount of d-c voltage
is required. Applications for non-controlled rectifiers include battery charging, motor-
field excitation, generator-field excitation, magnetic-chuck excitation, lifting-magnet
excitation, d-c control power supplies, etc.
The high-vacuum or kenotron rectifier tubes are inherently low-current tubes, because
the voltage drop and therefore the power loss in the tube are proportional to the current
flowing. High-vacuum rectifier tubes may be classified as low or high voltage. Low-
voltage types are used primarily for small amounts of d-c control power for other electronic
equipments. Often low-voltage tubes are constructed with two rectifying devices in one
tube, thus making a single tube suitable for a diametric (full-wave) rectifier circuit. High-
voltage types are used in such applications as dust precipitators and high-voltage power
supplies for other electronic equipment.
The outstanding characteristic of hot-cathode gaseous-type rectifier tubes is their
inherently low and constant voltage drop which results in high efficiency in high-current
applications. These tubes are available in a range of current ratings of 0.1 amp to 20
amp and from about 100 volts to 10,000 volts, peak inverse ratings. Low-voltage types,
such as are used in battery chargers, are usually filled with argon. Xenon-filled, argon-
and-mercury-vapor-filled, and mercury-vapor-filled tubes are used in applications requir-
CONTROLLED RECTIFIERS AND INVERTERS 21-09
ing 750, 2000, and 10,000 volts, peak inverse ratings, respectively. Gaseous-type rectifiers
will not operate successfully in parallel without load-balancing devices, because the tube
drop of two paralleled tubes may be slightly different and the tube with the lower drop
will carry all or most of the load current. A more complete discussion of hot-cathode
gaseous-type rectifier tubes of both the non-controlled and the controlled type is pre-
sented in Section 4.
Copper oxide and selenium-type metallic rectifiers are used predominantly in the low-
voltage high-current field. The general characteristics of these rectifiers are a relatively
low peak inverse voltage per rectifying disk and a relatively high current capacity. Stacks
consisting of one or more cells can be used in series or in parallel to increase their voltage
or current capacity, respectively. The copper oxide rectifier is older, from the standpoint
of general usage, than the selenium rectifier. The selenium rectifier can operate at a higher
temperature than the copper oxide rectifier, and therefore for a given rating it is a some-
what smaller unit than the copper oxide type. Selenium rectifiers are usually operated
nearer their breakdown voltage rating than copper oxide rectifiers; therefore the selenium
rectifier is usually more subject to damage on overvoltage. Other materials, such as copper
sulfide, exhibit the same rectifying action as the copper oxide and selenium materials but
are not as commonly used.
3. CONTROLLED RECTIFIERS AND INVERTERS
Controlled rectifiers generally are used whenever it is desired to adjust the d-c output
voltage level over a reasonably wide range, or when it is necessary to regulate the output
voltage to compensate for changes in the load current or changes in the input Line voltage.
Typical applications of controlled rectifiers are: (1) adjustable d-c voltage for motor- and
generator-field supplies; (2) adjustable d-c voltage for d-c motor armatures; (3) adjustable
d-c voltage for the d-c windings of saturable reactors which, in turn, control motor, light-
ing, or resistance power circuits; (4) adjustable d-c voltage supply for testing of various
d-c devices; (5) d-c power for charging capacitors in energy-storage resistance welders at a
given rate and to a given voltage.
In small rectifiers, it may sometimes be more convenient and economical to adjust the
rectifier d-c output either by adjusting the a-c voltage input or the d-c voltage output by
means of a slide-wire resistor. Also in large rectifiers it may be desirable to adjust the
output voltage by means of induction-voltage regulators, adjustable auto transformers, or
saturable reactors in the a-c circuit. If these methods are used, the rectifying elements
can be of the non-controllable type.
Grid-controlled thyratron rectifiers provide greater flexibility, faster response, and less
bulky control equipment than rectifiers controlled in the power circuits. Furthermore,
automatic control in larger sizes is generally more economical with thyratron control
than with power circuit control.
Thyratron-type rectifiers are always built in a single envelope. Some thyratron tubes
are controlled electromagnetically by a plate on the outside of the tube. By far the most
common practice, however, is to control the tubes electrostatically with a grid in the
electron path. Thyratron tubes can be obtained in ratings as low as approximately 20 ma
and have been built in ratings as high as 100 amp. (See Section 4.) The maximum size
of standard tubes, however, is about 12.5 amp. (High-vacuum triodes are generally not
used in controlled rectifier circuits.)
Controlled rectifier tubes may be connected in any of the circuits shown in Table 1.
Tubes and transformers, however, should be carefully selected so that the ratings are not
exceeded. As mentioned earlier, the peak and rms currents in a rectifier will be higher
on resistance and counter-emf loads than on inductance loads. Not only must this factor
be considered, but also consideration must be given to the higher peak and rms currents
that will result from the use of grid control on loads such as d-c motor armature circuits.
Another factor to be considered is the unbalance in tube currents which may exist in
polyphase rectifiers operating with rated current and having a large amount of phase
retard. Figure 1 shows the voltage and current wave shapes of a diametric (full-wave)
rectifier operating with varying degrees of phase retard on an inductive load, a resistive
load, and a fixed counter-emf load all having different electrical characteristics. Although
a diametric rectifier is used here for the sake of clarity, the same fundamental information
applies to other rectifier circuits. Although three different load classifications are shown,
many loads consist of various combinations of resistance, inductance, and counter emf.
The load current on a very highly inductive load is nearly constant even with a diametric
rectifier circuit. As the firing angle is retarded, the energy from the inductance is trans-
ferred back into the line circuit during a portion of the cycle when the tubes would be
21-10
ELECTRONIC CONTROL EQUIPMENT
normally non-conducting. When the firing angle has been retarded approximately 90°,
the inductance current is theoretically zero. Practically, however, the 90° firing point
will result in a current of approximately 10 to 20 per cent of the maximum which would be
expected as calculated by Ohm's law.
In a sense a purely resistance load is somewhat academic because this type of load
seldom occurs in practice. It is, however, a logical stepping stone in estimating what is
to be expected from counter-emf loads. It can be observed from Fig, 1 that the load
current hi a resistance load follows identically the wave shape of the output voltage.
Counter-emf loads fall into two general classifications: fixed and variable. A battery
is a typical example of a fixed counter-emf load. The peak value of load current in a fixed
counter-emf load is determined by the difference between the peak a-c voltage and the
counter-emf potential, and the circuit resistance. Exceedingly high current can be ob-
tained on low-impedance circuits with a very small difference in voltage between the load
Firing
full on
inductive load
Resistance load
Typical fixed counter-emf load;
FIG. 1. Rectifier Output Voltage and Load-current Wave Forms for Different Types of Loads and
with Several Degrees of Phase Retard with. Diametric (Full- wave) Rectifier
and the peak rectifier output. The inherent circuit impedance may reduce the peak cur-
rent to a reasonable value; if not, external resistance or inductance can be added for that
purpose. Figure 1 shows that as the firing angle of a rectifier on a fixed counter-emf load
is retarded there is, up to a certain point, no change hi the output current, but, beyond
the point where the transformer-secondary voltage and the counter-emf voltage intersect,
a reduction in current is obtained by a further retard in firing position. A d-c motor arma-
ture is a typical variable counter-emf load. This type of load is quite different in its opera-
tion from a rectifier or other fixed counter-emf load. A motor armature is a good example
of a load which includes resistance, inductance, and variable counter emf .
The thyratron rectifier circuits which have been described can also be used for inverters
to convert d-c power into a-c power, provided that both d-c and a-c power supplies are
available for the transfer of power and that the grid-control circuits are properly arranged.
Many motor-control rectifiers are operated as inverters during reversal of motor armatures
and during fast decay of the stored energy in generator fields. In these applications the
conventional rectifier circuit is used and the grid firing point is retarded to a point late in
the positive half cycle. In the high-power field, highly specialized inverters have been
built for several applications.
IGITCTRON RECTIFIERS. Ignitron rectifiers are ideaUy suited to their use in the
high-power field, because their cathodes — a mercury pool — can supply electron emission
for tremendous overloads. The maximum current is limited by the mechanical forces in-
volved and by the ability of the tube to deionize rapidly enough to prevent arcback.
Ignitron rectifying devices are made in capacities trom about 12 amp up to 1000 amp d-c
continuous rating. (In 1945 approximately 10 per cent of the central-station power gen-
THYBATKON AND IGNITRON CONTACTORS
21-11
erated in the United States passed through ignitron rectifiers.) Continuously evacuated
ignitron rectifiers are available in sizes as large as 6000 kw at 600 volts direct.
Figure 2 shows the efficiencies of ignitron rectifiers as compared with synchronous con-
verters and synchronous motor-generator sets. The rectifier efficiency increases with
higher voltage because the volt-
age drop across the arc in the
ignitron is nearly the same in
all cases, and, therefore, with
lower d-c voltage the arc drop
has a greater proportional effect
than at high voltage.
Thyratron rectifiers, like va-
cuum tubes, may be controlled
with very minute power levels
on the grid. An ignitron, how-
ever, requires a considerable
amount of power for a short
time for firing. This power may
be supplied either by magnetic
excitation circuits involving no
tubes and purely static control
devices, or they may be con-
trolled by electronic firing cir-
cuits involving thyratrons in
the ignitor circuit. The mag-
netic firing circuit is used where
the maximum of reliability is
required. Thyratron-type firing
93
94
90
82
I
74
70
•r-"
_-—
.
— -
-' —
.
S
Ig
"re
litre
ctifi
N
n
- —
— -
P4-
hron
-vJ
ous
con\
erte
__
— .
er
LV
< .-
""*
aync
/
/I
^x^
-""
,^^
--
•—
1'
/
^
^"
I/
/
*s*
>Sy
Sen
//
X
1
r/
i
//
— 1
500
-kw,
60C
•vol
t ap
Darat
us
1000-kw,' 250-voIt apparatus
40
60 80 100 120
Per cent full load, amperes
140 160
FIG. 2. Comparative Efficiencies of Power-conversion Units
circuits, however, may be less expensive to build, and also their inherently fast operating
speed may be more desirable for some applications.
4. THYRATRON AND IGNITRON CONTACTORS
Two controlled rectifier tubes of the thyratron or ignitron type can be connected in
inverse parallel and the combination connected in series with a single-phase load to make
a single-pole single-throw a-c switch called a thyratron contactor or an ignitron contactor.
Likewise, several pairs of tubes may be connected in polyphase circuits to make a poly-
phase single-throw a-c contactor. This type of contactor has several salient features:
1. In applications involving a very large number of operations, it eliminates the mechan-
ical wear and resultant maintenance of mechanical-type contactors. Furthermore, it is
quiet in operation.
2. This type of circuit is inherently fast in response. This means that power circuits
may be closed or opened more rapidly than with conventional magnetic contactors.
3. When these contactors are used with the proper phase control systems, they may be
fired synchronously at a given phase position in each half cycle to avoid the transient
currents that will result in inductive loads if the power circuit is closed at random.
4. These contactors may be used to control the effective a-c load voltage by adjustment
of the firing point. Control of load power can be obtained without power loss and without
undue voltage regulation due to load changes.
The choice of thyratron or ignitron tubes is dependent on the magnitude of power in-
volved. Typical applications of thyratron-type contactors are: (1) for controlling the
speed of some types of a-c motors; (2) for controlling the output voltage of high-voltage
transformers; (3) for low-power resistance welders; (4) for high-voltage resistance welders.
By far the largest number of applications of electronic contactors, however, has been
made in the resistance welding field, in which ignitron tubes are used.
General requirements for resistance welding are: (1) single-phase power; (2) power im-
pulses having a high peak value over a short period of time; (3) a large total number of
impulses over a given period of time; (4) control of the effective amount of welding current;
(5) controlled firing to eliminate transient currents. These requirements have made the
ignitron contactor with its extremely high peak-current capacity and its controllability
ideally suited to resistance-welding applications.
Figure 3 illustrates a typical single-phase ignitron contactor for resistance-welding serv-
ice. This contactor is of the simple on-off type. It is used to give faster operation than
magnetic-type contactors as well as to eliminate the maintenance on magnetically operated
21-12
ELECTRONIC CONTROL EQUIPMENT
mechanical contactors. Figure 4 shows an elementary circuit diagram, for an on-off type
ignitron contactor. This circuit operates as follows: When the initiating switch is open,
no current will now because power is not being supplied to the igniters for firing the tubes,
Assume now that the initiating switch is closed and that anode a is positive. Current will
not flow through the left-hand tube
until the ignitor has been fired.
The ignitor firing circuit starts with
anode a, continues through the
lower right-hand metallic rectifier,
through the water-flow switch, fuse, *
and initiating switch, and through
the upper left-hand metallic rectifier
into the ignitor which is immersed
in the mercury pool. Current flows
from this pool to the primary of the
welding transformer and back to
the other side of the a-c line. This
means that the entire line voltage
and the entire load current are avail-
able for firing the ignitor. With this
voltage and current available, the
ignitor fires the ignitron tube, and
then load current flows through the
main anode of the left-hand igni-
tron. When the anode 6 is positive,
ignitor firing current flows through
the lower left-hand metallic recti-
fier, through the initiating switch,
fuse, and water-flow switch; then
through the upper right-hand me-
tallic rectifier into the mercury pool
and back to the other side of the a-c
supply. The metallic rectifiers pro-
vide a path for the ignitor firing
current during the half cycle in
which a specific ignitor is to be
fired. During the other half cycle,
the metallic rectifiers prevent the
flow of reverse ignitor current which
would damage the ignitor.
Figure 5 shows how thyratron
tubes may be used to control the ignitron power tubes in order to obtain phase control
or synchronous timing control of the output power. A resistor is used in the anode of
the two thyratron tubes to limit the peak current flowing while a fuse is used to protect
the tubes against high rms current which would result if the ignitor were continuously fired
with no load current flowing.
FIG. 3. Single-phase Ignitron Contactor with Size D Tubes
(Courtesy General Electric Co.)
Welding < ( 1
transformed v» J
f Work
Fro. 4. Circuit Diagram for an Ignitron Contactor with Metallic Rectifier Firing
Figure 6 is a typical duty cycle rating curve for four sizes of contactors (ratings are for
two tubes) used on a 460-volt power supply. Three factors affect the amount of current
which can be handled by a pair of ignitrons: (1) The maximum current is a function of the
line voltage; for low line voltages, the tubes will carry a higher current than for high line
FUNDAMENTAL ELECTRONIC CONTROL CIRCUITS 21-13
voltages. (2) For a given line voltage there is a maximum rms current rating irrespective
of the length of time the current flows. (3) If the current flows over an appreciable length
of time, even though the duty cycle is low, the averaging time of the tube must be con-
sidered to prevent overloading the tube from a thermal standpoint. Per cent duty shown
in Fig. ' 6 indicates the percentage of total time that current is flowing through the tubes.
FIG. 5. Ignitron Contactor with Thyratron Firing Circuit
A pair of size D tubes has a continuous rating of 800 amp. As the duty cycle is reduced,
however, the maximum current can be increased. If the time involved is short, the rating
can reach almost 5000 amp. The size D tubes have an averaging time of 5.6 sec. This
means that, for any 5.6-sec period, the average current should not exceed 800 amp rms,
even though the actual current during conduction equaled 5000 anip. In other words,
the tubes could carry 5000 amp for approximately 0.9 sec (800/5000 X 5.6), provided no
D to 50C
Vc
Its
4000
3000
2000
|l500
|iooo
j? 800
"^ 600
sv
^s^
^ ».
V
S^£
X
X
^
"X^s
,
^
N
^
x
\
\
"X
— --S^
^~
\
\
£
| 400
300
200
mo
— -x^-
x^
s^
's <&t
S,
/i
weragi
ng tim
11 se
9 '
7.1 '
5f6 '
e
^s1^^
\y^
s,
s.
c.
"^X_
S
Size B
^
s^
S
S
Ize C
ize D
^>
ss
\
s
b
S
V
\
^
\
s
1 2 46
8 10 20 30 40 60 80100
Per cent doty
FIG. 6. Ignition-contactor Duty-cycle Rating Curve
current was carried during the remainder of the 5.6-sec period. If it were necessary to
have current flowing over a 5.6-sec period continuously, the tube rating would be the same
as for 100 per cent duty, or 800 amp.
FUNDAMENTAL ELECTRONIC CONTROL CIRCUITS
Because the applications of electronic control are so diversified and because most appli-
cations are highly specialized it is impractical to describe even a moderately complex circuit
with all its ramifications. An attempt will be made in this section to discuss several
fundamental control circuits which are commonly used in complete electronic systems,
with the hope that these circuits will be recognized when they are a part of complete
systems.
21-14
ELECTRONIC CONTROL EQUIPMENT
5. STABILIZED D-C CONTROL POWER SUPPLIES
Many electronic control equipments include a small d-c power supply usually consisting
of a diametric (full-wave) rectifier and a suitable filter. These are similar to the power
supplies used in radio receivers which are discussed in Section 7,
In order to provide stability of operation of the associated electronic control equipment,
it is often necessary to provide a d-c output voltage which is held constant irrespective of
line voltage or changes in load. This may be accomplished in several ways; the most
common are:
1. A-c voltage stabilizers. Figure 1 illustrates one typical type of automatic voltage
stabilizer circuit. The voltage-regulating action is due primarily to reactor 1 and the
parallel capacitor. When the line voltage is high, reactor 1, which operates near the
knee of the B-H curve, becomes saturated. Under this condition the reactor current
and the capacitor current are about equal, the total current being at about unity power
factor. As a result there is a voltage drop across reactor 2. When the line voltage drops,
Reactor 2
Variable
Input
voltage
Reactor 1 ;
Constant
output
voltage
Capacitor
+ '
rh Series
M regulating
resistor
D-c o
utput _
+
from filter /"J
— \ Regulating
V
'•/ glow
V.
S tube
Regulated
d-c voltage
FIG. 1. Circuit Diagram of A-c Voltage Stabilizer FIG. 2. Glow-tube-type D-c Voltage Regulator
however, the reactor current falls off more rapidly than the capacitor current. As a
result the current through reactor 2 is predominantly capacitive and there is a rise in
voltage across reactor 2. Units of this type will hold the output voltage to within =bl
per cent over about a ±15 per cent change in input voltage.
2. Gaseous-type voltage-regulating glow tubes. These tubes have inherently a constant
voltage drop. When the voltage has reached the ionization point a very small increase
in applied voltage will result in a comparatively large increase in tube current. These
tubes are well suited to control power circuits involving small currents. Three ratings
are most commonly used, namely, 75, 105, and 150 volts at 40 ma maximum. Figure 2
shows a regulating circuit, using a glow tube. The constant-voltage characteristic of the
glow tube will permit the rectifier output voltage to be increased or decreased, and the
voltage difference will be largely absorbed by the series regulating resistor. This results
in a nearly constant output voltage across the glow tube.
3. A series-type voltage regulator. This regulator uses a glow tube merely as a reference
voltage and involves a regulating principle which will be discussed later. This type of
voltage-regulating system will provide larger amounts of voltage and current and at greater
accuracy than can generally be obtained with the simple glow-tube arrangement discussed
before.
6. TIMING CIRCUITS
Timing circuits are widely used in electronic control systems. In many equipments
such as general-purpose timers, resistance-welder sequence timers, timers for cut-off
register applications which operate correcting devices for a given length of time, and
timing circuits which control the acceleration or deceleration rate of motors, timing is a
definite function. Often, however, the use of timing circuits may be incidental to the
function to be performed by a given equipment. For example, filter capacitors in d-c
control power supplies, capacitors across relay coils which are operated by half-wave
rectifiers, resistor-capacitor combinations, and electronic relays involving impulses of very
short duration which are used to maintain an operating signal long enough to operate a
magnetic relay are all energy-storage-type timing circuits.
A capacitor is used as a basic timing element in most timing circuits. Figure 3A shows
a simple series resistor-capacitor circuit. When the switch is closed, the capacitor charges
through the series resistor. The instantaneous voltage across the capacitor is expressed
TIMING CIRCUITS
21-15
Time
Switch
clcsei
Switch
<U L/opened
Time
FIG. 3. Basic R-C Timing Circuits
by the equation ect = E(l — e */rc), where t = time in seconds after the switch is closed.
Figure 3B shows a similar circuit in which the capacitor is charged almost instantly
(assuming that the d-c source has no resistance) and in which the capacitor discharges
through the parallel resistor. The instantaneous capacitor voltage after opening the
switch is expressed by the equa-
tion ect = E X e~i/ro. The above
equations will give the voltage
at any time. A more generally
used term, however, is the time
constant. The time constant is
defined as the time at which the
capacitor has charged to approxi-
mately two-thirds of its final
voltage value or the time at
which the capacitor has dis-
charged to approximately one-
third of its initial voltage value.
The time constant is expressed
as T — rCj where T = time in
seconds, r — resistance in ohms,
and C = capacitance in farads^.
Often a basic timing circuit will
include a parallel r-C circuit
with a resistor in series. This
will result in a time lag in the
charging circuit and a lag in dis-
charging as well,
r-C circuits are used in complete circuits to obtain a time delay by applying the capacitor
voltage to a tube grid to render the tube conducting or non-conducting at a given capacitor
voltage. Although different detail circuit arrangements are used in timing, the basic cir-
cuits shown are common to most electronic timers.
A general-purpose time-delay-relay circuit which uses a parallel r-C circuit for timing
is shown in Fig. 4. This is typical of complete timing circuits. The coil of the relay is
energized a definite time after switch S is closed. When switch S is open, the cathode of
the vacuum tube is connected through 2R (which is a relatively low resistance) to the
anode. Resistor 1R and the potentiometer P form a voltage divider across the a-c power
supply. With the switch open, the cathode is effectively connected to line 1 (through
resistor 2R) . Therefore current will now from line 3 through a section of the potentiometer,
through the parallel resistor-capacitor combination into the grid, and back through the
cathode. The grid in this instance acts as an anode since it is positive with respect to the
cathode during every other half cycle. The voltage drop across the timing resistor R
causes capacitor C to become charged. As capacitor C charges, the voltage applied to
the grid during alternate half cycles becomes less positive — the grid voltage is the alge-
braic sum of the a-c voltage and the
capacitor voltage. The capacitor will con-
tinue to charge until the voltage across the
capacitor is equal to the peak of the a-c
voltage from line 1 to the slider of the
potentiometer. If the potentiometer P is
turned to the extreme counterclockwise
position, this will be the peak line volt-
age. As potentiometer P is turned clock-
wise, the capacitor charges to a lower
value. When switch 5 is closed the
cathode is connected to the other side of
the line. At this instant the grid of the
tube is negative with respect to the cath-
ode by whatever potential the capacitor C
is charged. The instantaneous grid volt-
age, however, is a summation of the d-c capacitor voltage and the a-c voltage from line 3
to the potentiometer slider. Figure 5 shows the action of the capacitor discharge circuit
plus the a-c component. It can be seen that, when the switch is first closed, the grid is
sufficiently negative at all times so that no plate current flows. As the capacitor dis-
charges, however, the grid potential reaches a point where sufficient plate current flows to
energize the relay in the plate circuit. The capacitor C\ of Fig. 4 across the relay coil is
3 S 6
FIG. 4. General-purpose Time-delay-relay Circuit
21-16
ELECTRONIC CONTROL EQUIPMENT
used as an energy-storage device during the half cycle in which the tube is conducting so
that it can supply energy to the coil during the half cycle when the tube is not conduct-
ing, thus preventing the relay from chattering.
irid voltage
Timing
capacitor
voltage
A Tube
MM current
Switch
dosed
Time.
FIG. 5. Grid Voltage and Anode Current after
Timing Switch of Timer (Fig. 4) is Closed
> d
?SR
* +
J
(
L^
Tube 2
5>
D-c
r
[
-SUf
piy
Tube V-
J
SIgnaJ
r
N
.—
FIG. 6. Typical D-c Voltage Amplifier
7. D-C AMPLIFIERS
D-c amplifiers are commonly used in photoelectric controls, motor and generator con-
trols, electronic voltage regulators, regulated battery chargers, and other equipment
where it is desirable to amplify d-c signals. These amplifiers are generally not too well
suited for applications where the signal voltage is low and where a high degree of ampli-
fication is needed, because the instability of the tube characteristics can result in output
variations equal to or greater in magnitude than would be obtained from a complete input-
signal range. D-c amplifiers are very well suited, however, to regulating circuits where the
difference between two fairly large voltages is applied to the grid circuit. Regulating
circuits will be discussed in more detail later.
Figure 6 shows a typical d-c voltage amplifier. Resistors IE and 2R form a voltage
divider which establishes the cathode potential of tube 2. Resistors 3/jJ, 4R, and 5R are
chosen so that, when plate current is not flowing in tube 1, the grid of tube 2 is positive.
When current flows through tube 1, the additional IR drop in resistor 3R lowers the grid
voltage of tube 2 and reduces its plate current. In the plate circuit of tube 2 is shown a
saturable reactor which could be used in a thyratron phase-shifting circuit, although any
voltage- or current-responsive device could also be used here. If the signal voltage were
zero, the grid of tube 1 would be at cathode potential and tube 1 would be carrying approx-
imately maximum current. As the grid voltage of tube 1 is made negative, the plate
current of tube 1 would decrease, thus increasing the plate current in tube 2.
8. A-C AMPLIFIERS
In control circuits a-c amplifiers are usually of the capacitance-coupled type. Though
in some circuits they are used in much the same way as in radio circuits they are often
employed in circuits in which it is desirable to amplify an impulse signal. For example,
in photoelectric cutoff or web-register control systems used in cutting bags or labels at a
particular point with respect to the printed material it is desirable for the equipment to
respond to small marks on paper which is moving at high speed. The light impulse is
obtained by scanning the paper surface with a photo tube. The normal light level may
be relatively high, and the mark on the paper may correspond to only a small change in
light. Therefore, it is necessary to have a very sensitive amplifier which responds only
to rapid light impulses or changes and not to steady-state light or general changes in
light level.
REGULATING CIRCUITS
21-17
7R
2C .
M, '
INTube 1
r
V
I Relay
sjube 2
A typical impulse amplifier is shown in Fig. 7. Resistor IR, 2R, 3R, and 4R constitute
a voltage divider to supply the various^voltage levels required in the circuit. The proper
grid bias on tubes 1 and 2 is supplied through grid resistors 6R and 8R respectively.
Assume that a steady level of light is
applied to the phototube. The circuit Reset
constants are arranged so that under
this condition current flows in tube 1
but not in tube 2. Now if light sud-
denly is diminished the phototube
current is reduced and capacitor 1C
momentarily "pulls" the grid of tube
1 to a more negative position. This
immediately reduces the plate current
in tube 1, which in turn raises mo-
mentarily the grid voltage of tube 2
through capacitor 2(7. Tube 2 is a
thyratron type and has a d-c anode
supply voltage. Therefore although
its grid voltage may go in the positive
direction only momentarily this is
sufficient to fire the tube and once
fired it remains conducting until the
reset contact shown is opened.
D8R
FlQ. 7. Typical Impldse.type A.c Amplifier M Used
Photoelectric Cutoff Register Controls
9. REGULATING CIRCUITS
Regulating circuits are used in many applications where it is desirable to hold quantities
such as voltage, current, speed, position, pressure, temperature, and the like constant
irrespective of conditions, such as load or line-voltage variations, which would normally
cause the quantity being held to deviate from the desired value. Any regulating circuit
has four fundamental requirements :
1. A standard or a reference voltage, which is held constant at all times and which
represents a value against which the quantity to be held constant is compared. The refer-
ence voltage is the heart of a regulating circuit because the accuracy of the regulator can
never be more accurate than the reference voltage.
2. Means must be provided so that the quantity to be regulated will produce a signal
voltage which can be compared with the reference voltage.
3. An amplifier, to amplify any difference that may exist between the regulated]quantity
and the reference voltage.
4. A controlling means, which will operate from the amplifier to restore the quantity
to approximately the yalue originally held before the deviation occurred.
Figure 8 shows an electronic voltage regulator, the purpose of which is ,to supply a
constant d-c voltage output over a wide range of load current and d-c input line voltage.
The total output power from this circuit is limited by the current that can be handled
by the 2A3 tube shown. (Parallel tubes or other tube types will deliver more power.)
Assume for the moment that switch S is open and also that no current is flowing in the
plate of the 6J7 tube. Under these conditions, the grid of the 2A3 tube will be at approxi-
mately cathode potential. The effective resistance of the 2A3 tube under this condition
is very low. Therefore a high voltage will exist across lines 2 and 3. Resistors IR and 2Rt
which are in series with the OA3/VR75 glow tube, are such that with rated regulated d-c
output voltage the glow tube will ionize and, once ionized, will conduct a small amount of
current. The characteristic of the glow tube is such that, if the voltage between lines 2
and 3 is varied, the voltage across the glow tube will remain reasonably constant. How-
ever, the more constant the voltage across lines 2 and 3 can be held, the less variation
there will be in the voltage across the glow tube because the voltage across the glow tube
changes somewhat with current. Since the objective of this equipment is to hold the
voltage output constant, the reference voltage must be held as constant as possible.
The cathode of the 6J7 amplifier tube is connected to the glow-tube anode, point 4.
Resistors 3R and 4# constitute a voltage divider across the output of the regulator and
therefore provide a signal to the grid of the 6J7 tube which is proportional to the output
voltage. Resistors 3JK and 4JS are selected so that with rated regulated d-c output voltage
the grid of the 6J7 tube will be at approximately cutoff. The actual grid signal consists
of the difference between the voltage across resistor 4.R and the voltage across the glow
tube. If it is assumed that the reference voltage from the glow tube is constant, then
21-18
ELECTRONIC CONTROL EQUIPMENT
any deviation in output voltage will be reflected as a difference in the potential between the
grid and the cathode of the 6J7 tube.
As was stated before, if no current is flowing in the 6J7 tube, the effective resistance
of the 2A3 tube is very low. The output voltage between lines 2 and 3 therefore will be
Load
FIG. 8. Electronic D-c Voltage Regulator
high. This, however, results in a grid-to-cathode voltage on the 6J7 tube of a sufficiently
high positive value to cause the 6J7 to conduct plate current. This current causes an
IR drop between lines 2 and 7 across resistor 5R, and causes the grid of the 2A3 tube to
assume a negative potential. This negative potential increases the effective resistance
of the 2A3 tube and thus reduces the output voltage between lines 2 and 3. There is a
certain grid-to-cathode voltage on
the 2A3 tube which will result in an
output voltage across lines 2 and 3
sufficient to adjust the grid potential
of the 6J7 tube to give the desired
grid-to-cathode voltage on the 2A3
tube.
If now the regulator is holding a
given voltage and load is added by
closing the switch S, the output volt-
age between lines 2 and 3 will im-
mediately drop because the effective
resistance of the 2A3 tube is in series
with the load. In order to correct
this low-voltage condition, the regu-
lator must again go into action.
When the output voltage is reduced,
the grid voltage is made more nega-
tive with respect to the cathode
voltage on the 6J7 tube. This more
negative value of grid voltage re-
duces the 6J7 plate current and
thereby makes the 2A3 grid less neg-
ative, which reduces the equivalent
resistance of the 2A3 tube, again re-
storing the correct output voltage.
The curves of Fig. 9 show input
^
X,
""**
X
X
xj{
put
volt
300
"^
X,
*x
».
120
^X
"X
x
^
"***
100
±5
°
\
6J
7 pic
nicrc
te c
)am
urre
Dere
nt
;)
0
• 250
1
80
X
V.
s^
60
X
X
s
40
200
Re
jula
ed i
5Utp
Jt V
alts
N
20
170
Q
)
1
0
2
0
3
0
FIG. 9.
Performance of Electronic Voltage Regulator
Shown in Fig. 8
Load mtlliamperes
and output voltage as a function of
load current for the regulator. It
also shows the plate-current change
required of the 6J7 tube to give accurate regulation of the output voltage. It can be seen
that, for a wide change in output load current and for a wide change in input line voltage,
the regulated output voltage is held nearly constant.
The electronic voltage regulator just discussed is a simple unit when compared with most
THYRATRON GRID-CONTROL CIRCUITS
21-19
complex electromechanical regulators; however, it is typical of all regulating circuits in
that it includes the fundamental elements of a regulating circuit.
The essential regulating elements can be explained as follows: Referring to Fig, 8, the
voltage across the glow tube between lines 3 and 4 is the standard or reference voltage.
The voltage across lines 3 and 6 is the signal voltage. Any difference between the voltages
4 to 3 and 6 to 3 is applied to the grid of the 6J7 tube, which amplifies the existing devia-
tion. This in turn controls the grid on the 2A3 tube to correct for the voltage deviation.
An important feature of a regulating circuit, as far as obtaining accuracy is concerned, is
the use of two relatively large voltages in the comparison circuit. This can be shown best
by an example. If the 6J7 tube required 0.1-volt change on the grid to effect a complete
swing of the grid of the 2 A3 tube, this 0.1-volt change can be accomplished on a 200-volt
output circuit with a 75-volt reference voltage by approximately a 0.3-volt total error
in the output. In other words, the inherent regulating error of the system does not exceed
0.3 volt out of 200 volts or 0.15 per cent for a wide load and input line-voltage change.
Furthermore, if the inherent tube characteristics varied in such a manner that a given
6J7 plate current resulted with a grid voltage 0.3 volt different from the original voltage
the output voltage would again be in error by only approximately 0.15 per cent. If lower
voltages were used, both errors would increase.
10. THYRATRON GRID-CONTROL CIRCUITS
Thyratron tubes are used in circuits having d-c or a-c anode supplies. When they are
used with d-c supplies they are on-off devices and a simple d-c grid-bias control can be
used to fire the tubes. In a-c cir-
cuits, such as rectifiers or electronic . ^Anode voltage
contactors, however, it is usually
desirable to control the effective
output voltage by controlling the
point in each cycle at which a par- 0
ticular tube fires.
When a thyratron is connected
to an a-c power supply the anode
voltage is different at each point
in the cycle. Therefore at the be-
ginning of a positive-voltage half
cycle a positive value of grid volt-
age is required to fire the tube. As
the anode voltage increases in the positive direction, the grid voltage required to fire the
tube becomes negative. Figure 10 shows a curve of the grid voltage — the critical grid-
voltage curve — required to fire a thyratron tube on an a-c power supply. Figure 1QA
shows that with an a-c. grid voltage applied 180° out of phase with the anode voltage the
tube does not conduct. Figure 10B shows that with an a-c grid voltage applied in phase
with the anode voltage the tube conducts for the entire half cycle. Figure IOC shows
that with the a-c grid voltage lagging the applied voltage by 90° the tube conducts for
half of the half cycle.
Although a number of different types of grid-controlled circuits can be used for con-
trolling the output voltage of thyratron tubes, the most widely used control circuits are:
(1) grid-voltage phase shifting; (2) fixed 90° phase shift with adjustable d-c bias.
Critical
grid
voltage
(A) (B) (C)
Zero output Full output Half output
voltage voltage voltage
FIG. 10. Method of Grid Contiol of Thyratron Tubes
FIG. 11. Basic Circuit for Controlling Thyratron Tubes with Adjustable Grid-voltage Phase Angle
Figure 1 1 shows the basic circuit for a method of controlling thyratrons by means of an
a-c grid potential whose phase angle can be adjusted. The grid-voltage phase position is
21-20
ELECTRONIC CONTROL EQUIPMENT
determined by the ratio between the variable inductance and the fixed resistance shown
in the primary of the grid transformer 2T. Figure 12 shows the vectors of the voltages
involved in the grid circuit. EI is the anode-transformer secondary voltage. Ir is the
voltage across the resistor and is in phase with the resistor-reactor series current. !XL is
the voltage across the variable reactor. The actual grid
voltage Eg can be seen to vary in phase position, but
not in magnitude, as IXL is changed (change in the re-
actance). The variable reactor could be an iron-core
reactor with a removable plunger, or a small saturable
reactor, the d-c winding of which could be energized by
a vacuum tube or other means. It is also possible to
use a fixed capacitor and a variable resistor to obtain
this same type of control. Another method of obtain-
ing this same type of control is by the use of a selsyn
(induction phase shifter) which has a three-phase
primary stator and a single-phase secondary rotor. As
the rotor is turned, the rotor output voltage, which can be applied directly to the grid
circuit, changes in phase position.
Figure 13 shows the basic circuit for obtaining a fixed a-c voltage phase shift plus an
adjustable d-c voltage for controlling the thyratron firing point. The voltage Eg can be
seen to be made up of two components: Ez, having a magnitude which is determined by
the ratio of transformer 2T, and a phase position which is determined by the ratio of
resistance and capacitance in the primary of transformer 2T; and an adjustable d-c
PIG. 12. Vector Voltages of Phase-
shift Circuit of Fig. 11
90° lagging
a-c grid potential, Eg
FIG. 13. Basic Circuit for Controlling Thyratron Tubes with Fixed A-c Voltage Phase Shift plus Ad-
justable D-c Grid Voltage
potential EI. With this circuit, grid control is obtained by adjusting the d-c grid poten-
tial EI. Figure 13 shows firing full on with positive grid voltage and nearly full off with
negative grid voltage. Smooth control can be obtained over the entire range.
COMPLETE ELECTRONIC DEVICES
Many electronic circuits can be built into complete electronic devices, the operation of
which is independent of associated equipment. Timing relays, electronically regulated
power supplies, rectifiers, and electronic contactors are complete electronic devices which
have been discussed previously.
11. ELECTRONIC RELAYS
CONTACT-OPERATED ELECTRONIC RELAYS. Contact-operated electronic relays
are used where it is desirable to operate a magnetic contactor or other electrically operated
device upon the closure of a circuit which has insufficient current-carrying capacity to
operate the final or an intermediate device. For example, it is often desirable to have a
power circuit initiated when an instrument pointer reaches a certain mark on the scale.
The pointer contacts in most cases are not only inadequate to carry the power in the load
circuit but also inadequate to carry the power required to actuate a contactor in the load
circuit. The contacts, however, are adequate for insertion in the grid circuit of an elec-
tronic relay, which will in turn initiate a magnetic contactor. Other applications of this
type of relay are: (1) liquid-level controls where the liquid itself is the conducting me-
ELECTRONIC RELAYS
21-21
Typical Circuit Diagram for Contact-
operated Electronic Relay
dium — in this case a pump or a valve is operated by means of the relay; (2) high-low
gaging _ of small parts where the parts passing between contacts carry the grid signal
which in turn operates the relay to actuate reject devices; (3) drop-switch circuits in
textile mills to operate signals which indicate broken "ends" of yarn.
Figure 1 shows a typical circuit diagram
for a contact-operated electronic relay.
When the switch S is open, the transformer
secondary supplies power through the half-
wave rectifier to charge capacitor 2C. At
the same time the grid of the amplifier tube
is at cathode potential. The triode tube
conducts full current and relay CR is en-
ergized. When the switch S is closed, the
grid of the amplifier tube is brought to a
negative potential and the relay CR is de-
energized. By the proper choice of resis-
tors 1C, IR, and 2R, this circuit will operate
with resistances as high as 10 megohms
across the switch terminals. Also, with
other resistor and capacitor values it will
operate when the switch circuit is closed yIG>
only long enough to give a very short im-
pulse for charging capacitor 1C.
PHOTOELECTRIC RELAYS. Photoelectric relays are often used as limit switches
for operating signals, counters, or other devices in applications where mechanical limit
switches would be unsuitable because of an excessive number of operations, because of
extremely high velocities of moving articles, because of temperature extremes or because
the material which is to operate the device has insufficient mechanical strength to operate
a mechanical limit switch. There are also many photoelectric-relay applications which
are unique to light-responsive devices, as indicated by the following examples: (1) oper-
ation by the light reflected by or transmitted through certain colors of material; (2) oper-
ation by the amount of light
transmitted through holes in
cloth, paper, steel, or other
material; (3) operation by
light reflected from certain
types of bottle cracks.
Figure 2 illustrates an in-
genious application of a sim-
ple photoelectric relay. A
motor-driven screwdriver is
used to make an adjustment
on a relay contact. When
the contact opens, an indicat-
ing light is turned on. A
phototube is held over the
indicating light to shut off
the motor-driven screwdriver
automatically when the light
comes on, thus assuring
proper adjustment of the
relay.
A number of special and
general-purpose types of
photoelectric relays are com-
mercially available. FigureS
shows several general-purpose
photoelectric relays: 1 is an
FIG. 2. Application of Photoelectric Relay to Motor-operated out(jOOr-type weatherproof
Screwdriver (Courtesy General Electric Co.) relay* 2 is an indoor-type
high-sensitivity relay with a large light-collecting lens; 3 is a high-sensitivity relay with a
separately mounted phototube; 4 is a simple general-purpose relay; 5 is a general-purpose
relay with a separately mounted phototube. w
Figure 4 shows the circuit diagram for the general-purpose relay, numbered 4 in Fig. 3.
Assume that light is not shining on the phototube and that the slider of potentiometer P
\
21-22
ELECTRONIC CONTROL EQUIPMENT
is turned completely counterclockwise. Therefore the full voltage of the lower transformer
secondary is connected from the cathode to the grid circuit. During every other half
cycle the grid circuit becomes positive. This charges the grid circuit capacitor by grid
rectification in the direction indicated. The grid circuit is positive during the half cycle
FIG. 3. General-purpose Photoelectric Relays (Courtesy General Electric Co.)
in which the plate is negative. Thus no plate current flows. When the plate circuit is
positive, the polarity of point A is negative; also the charge on the capacitor is in a direc-
tion to make the grid even more negative, thus preventing the relay from being energized.
Now, if light is applied to the phototube, current flows through the phototube and capacitor
in the direction of the arrow during the half cycle in which the grid is negative. This
effectively discharges the capacitor in proportion to the amount of light on the phototube.
If sufficient light is applied to the photo-
tube, the capacitor charge due to the
phototube will be greater than the charge
due to grid current and the grid will
become positive, thus energizing the
plate-circuit relay. When the potenti-
ometer slider is in the counterclockwise
position, the capacitor charges to a
higher value than when it is turned clock-
wise; therefore more light is required to
operate the relay in the counterclockwise
position of the slider than in the clock-
Sbti'onary operating vane
wise position.
FIG. 4.
Circuit Diagram of Relay 4
Fig. 3
FIG. 5. Oscillator-type Elevator-leveling Relays
Mounted on an Elevator Car (Courtesy General Elec-
tric Co.)
^ The a-c operated type of photoelectric relay just described is not suitable for applica-
tions where the light impulses are of extremely short duration, because an impulse may
occur during the time when the sine wave of anode potential is passing through zero and
therefore the relay would not be energized. Impulses of light for a-c operated relays must
be at least in excess of 1 cycle. In order to operate relays where the light impulses are of
RESISTANCE-WELDER CONTROLS
21-23
extremely short duration, it is essential to use a d-c power supply for the anode power of
the amplifier tube, as well as for the photoelectric tube itself. The circuit diagram of a
high-speed photoelectric relay is shown in Fig. 7, p. 21-17.
ELECTROMAGNETICALLY AND ELECTROSTATICALLY OPERATED OSCIL-
LATOR-TYPE RELAYS. The electro-
magnetically operated oscillator-type relays
were probably first used industrially in the
leveling of elevators. Figure 5 shows a
typical installation of five elevator-leveling
relays mounted on an elevator car. Fig-
ure 6 shows the connection diagram for this
unit. When there is no magnetic material
in the oscillator coil circuit, the tube current
is low and the relay CR is de-energized. As
the car approaches a floor, however, an iron __
channel enters the oscillator-coil magnetic •& 0 ,-,. ., . ^ .,, , T-,, , , """,.
. ., , .„ ,. , mi- • FIG. 6. Circuit of Oscillator-type Elevator-leveling
circuit and oscillation stops. This increases Relay
the oscillator plate current and energizes
the relay CR which in turn operates the necessary control equipment to stop the car at
the desired level.
Figure 7 illustrates the use of an oscillator-type relay which is used in a pyrometer con-
troller. An iron vane on the instrument pointer passes through the oscillator coil and
energizes a 15-amp control relay when the pyrometer reaches a predetermined tempera-
ture. The point at which the oscillator stops oscillation is very sharp and gives a high
degree of control accuracy. Also since no mechanical forces are involved, such as there
would be with mechanical contacts, the accuracy of the instrument is not impaired.
Electrostatically operated oscillating-type relays are used as level controllers in grain
bins and in tanks which store non-conducting liquids.
^Control polofrspottfer
•pyfometej pofnter
inrrdl circuit coils
•Pin jacks for control coils
-Load relay
Oscillator coifs
Vacuum, tube
FIG. 7. Free-vane Electronic Pyrometer Controller (Courtesy The Bristol Co.)
12. RESISTANCE-WELDER CONTROLS
The first large-scale applications of electronic control industrially were made in the
resistance-welding field. Electronically controlled resistance welders produced results in
welding which were previously impossible. Thus a highly specialized branch of control
21-24
ELECTRONIC CONTROL EQUIPMENT
has been developed to meet the many requirements of resistance welders. Resistance
welders are divided into three primary types: (1) spot or projection welders; (2) seam or
roll-spot welders; (3) upset or flash welders. Most electronic welder-control equipments
are used on spot, projection, and seam welders.
The sequence of operation in making a spot weld is as follows: (1) The welder electrodes
are applied to the metal during the "squeeze" time. (2) Welding current is passed through
the material for a predetermined "weld" time. (3) The electrodes are held closed during
a "hold" time, while the material hardens. A pulsation spot weld is made in the same
manner as a spot weld except that during the "weld" time the power is intermittently
applied with cooling intervals between the power intervals. Seam welds are overlapping
or non-overlapping welds made consecutively by intermittent power pulses while the
material is passing between two welding wheels.
Most welder controls consist basically of a thyratron or ignitron contactor connected
in the primary of a welding transformer. Welding power levels vary from a few hundred
volt-amperes for small parts to values in excess of 1000 kva for heavy parts and structures.
Because the resistance of the material being welded is very low, a very high secondary
current (1000 to 100,000 amp) is required to produce a weld. The relatively long secondary
"loop" which is used, in combination with the low resistance of the secondary circuit,
results in a low power-factor load.
From a power-system standpoint, a single-phase load with such high peak-power
demands of very short duration is sometimes a disadvantage. Energy-storage-type welder
controls store energy either in capacitors or in an inductance during the non-welding time
and "dump" the stored energy into the material to produce a weld. These controls have
three advantages over the conventional single-phase controls, particularly when used in
welding aluminum or other high-kva-demand materials: (1) The control operates from a
three-phase power supply. (2) The peak-power demand is low. (3) The power factor is
higher than for most single-phase controls. Energy-storage type of controls are more
expensive and less flexible than single-phase controls, and their general acceptance is
thereby limited.
The simplest form of electronic control for resistance welders is the single-phase thyra-
tron or ignitron contactor described previously. This provides high-speed operation and
low maintenance, but it is simply an on-off power control. Current starts to now when
the initiating switch is closed, and it stops flowing at the first current zero after the initi-
ating switch is opened. The energy in watt-seconds which is delivered to a weld = PUT.
The resistance R is dependent on the material being welded. For a given resistance the
welding current I is directly proportional to the effective voltage. With an on-off type
control the current can be changed only by adjustment of transformer taps. Often manual
or mechanical timers are used with ignitron contactors to control the time T.
In some cases the approximate adjustment of current magnitude provided by tap-chang-
ing combinations on the welding transformer are sufficient. However, certain metals and
alloys which must be welded rapidly (within a narrow temperature range) require more
accurate current settings. Phase-shift heat-control equipment can be added to ignitron
contactors to provide these accurate settings. Figure 8 shows oscillographs of welding
currents under three conditions of heat control.
Primary
current
^
A
V
V
Secondary |/\
cur re at """— f — *"
A
A
^A
V
V
Line
voltage
A. A
V V
V V
V V
« Low heat Moderate heat I Maximum heat
FIG. 8. Oscillograms of Current in Welder when Using Phase-shift Heat Control
Automatic weld timers are often used with electronic contactors to coordinate the
various mechanical operations as well as to time the welding power impulse. When
welding thin-gage materials, the required time of current flow may be as short as 2 cycles.
A variation of 1 cycle would mean a variation in the heat input of 50 per cent and could
RESISTANCE-WELDER CONTROLS
21-25
FIG. 9. Oscillogram Made When Current is Started at
Zero Point on Voltage Wave
give a faulty weld. Therefore precision-type timers are required. On the other hand, if
the welding time required were 30 cycles a precision timer would not be so important
rJlnteSr S68 ^1^^ in^ated at a n°rmal CUrrent 2ero a tra^*t Current will be
present which will result m additional heat in the weld. On short time intervals the
transient may add considerably to the total heat. Variations in welds will therefore result
from random firing. Synchronous firing is often provided to minimize the transient cur-
rent by firing the power tubes at a fixed point in the cycle. Figure 9 shows the transient
current which will exist when current is started at the zero point on the voltage wave.
Figure 10 shows how the transient can
be eliminated by starting the current at j*-Start-zero point on voltage wave
a normal current zero. '
Figure 11^1 illustrates a circuit which
will provide phase-shift heat control and
synchronous firing. The thyratron fir-
ing circuits on both tubes are identical
except for the instantaneous polarities
of the transformers in the grid circuits.
The instantaneous polarities indicated
exist when the anode of the left-hand
thyratron tube is positive. Figure 1 IB
shows the supply voltage E and the
grid voltage. The grid voltage consists
of two components: (1) EB, which is
the voltage of 3T secondary; (2) EP,
which is the voltage of IT secondary.
Transformer IT is a "peaking" transformer which has only a small amount of iron in
the core. This results in saturation at a particular point in the wave and therefore
a peaked output voltage, about 5° or 10° wide. The phase position of the voltage
applied to the peaking transformer and therefore the phase position of the voltage peak
is adjusted by the phase-shifting rheostat 1R. The magnitude of Ep when added alge-
braically to Eb is insufficient to fire the thyratrons. Figure HCt however, shows the grid
voltage when switch SW is closed. The secondary voltage Ec of 2T is of a polarity that
subtracts from EB. Voltage Ep is now of a sufficiently high value to fire the thyratrons.
During the half cycles when the grids are positive, the grid capacitors are charged in the
direction indicated. This provides a small negative grid bias to prevent misfiring at the
beginning of a cycle when the a-c grid voltage is going through zero.
A complete welder control can be made up of a number of individual components, or
complete control units can be obtained which include some or all of the above features.
Figure 12 is an elementary diagram of a spot-welder control that provides precise timing
of the weld impulse, as well as synchronous firing. It does not provide phase-shift heat
control. The control essentially is made up of a d-c control rectifier (not shown), a
"keying" tube to insure starting the
j<rStart-m!niroum transFent point power flow at the desired point in the
1 on voltage wave voltage cycle, a timing circuit which is
1 /\ /\ /\ also a leading firing circuit, a trailing
firing-control circuit, and an ignitron
power circuit. The keying tube is nor-
mally held non-conducting by the nega-
tive bias across resistance 2.5. It is fired
at a particular point in the wave as de-
termined by the adjustment of resist-
ance 4R in series with the primary of
the peaking transformer. When the
initiating switch SI is in the 1 position,
the grid of tube 2 is negative. After
the initiating switch is closed in the 2
position, and at the proper time in the
next cycle, the grid of tube 2 is made sufficiently positive so that it conducts. This in turn
fires the ignitron power tube. As capacitor 2C charges (the time being dependent on the
setting of resistance 6R) , the grid of tube 2 becomes less positive. At a given time, tube 2
will again have a negative grid voltage and therefore will not fire the ignitron. On an in-
ductive load (a welder load), the current in the left-hand ignitron tube will still be flowing
when the voltage applied to the right-hand ignitron tube becomes positive. This means
that, as the current in the left-hand ignitron goes to zerp, the feedback transformer will
put a positive voltage on the grid of tube 3, thus making the right-hand ignitron tube
FIG. 10. Oscillogram Made When Current Flow is
Started at the Normal Current Zero by Synchronous
Firing
21-26
ELECTEONIC CONTKOL EQUIPMENT
Secondary*? - EB +
3T Secondary
A-c supply
ST 7 a 2T ^ Prlmaty
Primary] /Prlmaryf
(A)
IT
Secondary
3T Secondary
Vr
Wio)
S open ^closed
FIG. 11. Phase-shift Heat Control and Synchronous Firing is Provided by the Circuit
FIG. 12. Circuit of Welder Control Having Precise Timing and Synchronous Firing, but without Heat
Control
D-C MOTOR CONTKOL
21-27
conduct for a half cycle For each half cycle which the left-hand ignitron tube fires,
there will be duplicate firing on the right-hand ignitron tube. This circuit provides a
means of controlling two tubes with different cathode potentials from a single timing
source. Furthermore, it eliminates the possibility of obtaining an odd number of half
cycles of power, which would cause saturation of the welding
transformer. This circuit, however, cannot be used for heat
control.
Figure 13 shows a fully electronic welder-control panel.
The top section includes an electronic sequence timer for
timing the various parts of the machine cycle. The center
section includes a synchronous precision weld timer and phase-
shift heat control. The bottom section is an ignitron contactor.
13. D-C MOTOR CONTROL
Electronic adjustable-speed drives for d-c motors have been
applied in many industries. Typical of these applications are :
(1) drives for several types of machine tools, including lathes,
grinders, and milling machines; (2) paper-machine drives;
(3) rubber-calender drives; (4) conveyor drives; (5) textile-
range drives; (6) steel-mill auxiliary drives; (7) testing-equip-
ment drives.
In many applications the entire motor power is supplied
through electronic rectifiers of the controlled type. The thy-
ratrons are then usually controlled from vacuum-tube control
circuits. Most applications involving electronic power sup-
plies have been made in the low- and medium-horsepower
field, between !/4 and 30 hp. Although some applications of
electronic power supplies have been made as high as 300 hp,
the more conventional power converter in the large size is a
motor-generator set. In some motor-generator-set applications,
thyratron rectifiers are used to control the field of the genera-
tor or the motor or both, as necessary. High-vacuum tubes
are then generally used to control the thyratrons. In other
applications electronic control is limited to the use of vacuum
tubes for controlling the low-power fields of pilot exciters, such
as the General Electric amplidyne, which in turn control the
generator or motor-field power.
Figure 14 is a typical electronic control circuit which pro-
vides adjustment of the armature voltage of a d-c motor by
thyratron phase-shift control to obtain speed control. Figure 15 shows pictorially the
essential components of a complete adjustable-speed drive. This drive provides the fol-
lowing features: (1) adjustable motor speed over a wide range from an a-c power supply;
(2) accurate speed regulation; (3) current-limit acceleration to a preset speed; (4) com-
pensation for the internal motor IR drop, regardless of motor load; (5) normal motor
torque at the instant of closing the motor-armature contactor.
The motor field is supplied by a non-controlled rectifier (not shown). D-c control
power is obtained from a small control-power rectifier (not shown). The a-c winding of
the saturable reactor SR, the d-c winding of which is shown, is connected in the
thyratron phase-shifting bridge to adjust the rectifier output voltage in proportion to
the amount of current in the d-c winding. Tubes 1 and 2 are voltage-regulating glow
tubes. The speed-control potentiometer IP which is connected across the lower glow
tube (tube 2) provides a reference voltage against which the motor-armature voltage is
compared.
Conventional glow-tube voltages are 75, 105, and 150 volts. The d-c motor voltages
are commonly 230 volts. Therefore a voltage divider is connected between lines 24 and 26
so that the voltages between lines 22 and 7 will be about equal to the reference voltage
when the motor-armature voltage is 230. The voltage from lines 22 to 7 includes an IR
compensation voltage which will be discussed later. For the moment, however, assume
that the IR compensation potentiometer, 3P, is turned counterclockwise so that 26 and 7
are at the same potential. Any difference in voltage which exists between the slider of
the speed control and point 22 is applied to the grid of tube 4. A capacitor is connected
from grid to cathode of this tube to filter the rectifier output voltage before it is applied
to the grid.
L
FIG. 13. Fully Electronic
Welder Control Having Pre-
cise Timing and Synchronous
Firing, but without Heat
Control (Courtesy General
Electric Co.)
21-28
ELECTRONIC CONTROL EQUIPMENT
If the armature voltage is proportionally lower than the speed-control slider voltage
the grid of tube 4 will be negative with respect to the cathode and therefore tube 4 will
conduct no plate current. This results in a lower voltage drop through resistor 2R and,
consequently, a less negative voltage on the grid of tube 3, which increases the plate
current of tube 3.
The increased plate current which flows through the d-c winding of SR increases the
rectifier output voltage until the grid voltage of tube 4 differs from the cathode only by
the voltage required to produce the desired rectifier output voltage. A small grid-voltage
change will result in a range of output voltage from 0 to maximum. If the speed-control
slider is moved, therefore, there exists momentarily a large differential voltage applied
to the grid. This will turn the power tubes entirely on or off, as the case may be, until
lurrentVVW vwJ
FIG. 14. Typical Control Circuit for Electronic Motor Control
the armature voltage has reached the new level. Once it has reached the new level only a
small difference between reference and signal voltage is needed to control the rectifier.
If the field current of a d-c motor is held constant the no-load speed is proportional to
the applied voltage. When mechanical load is applied to the motor shaft, however, the
armature current is increased. This results in a voltage drop in the internal motor-arma-
ture winding which reduces the speed in proportion to the voltage drop. A small motor
may have a drop of 23 volts at full load. This is 10 per cent of the rated armature voltage
of a 230-volt motor. At rated applied voltage then there will be a speed regulation of 10
per cent between no load and full load. At 10 per cent of speed and no load, however, the
applied voltage is only 23 volts. If this voltage is held constant the speed will be reduced
to 5 per cent at 50 per cent of load and further reduced to 0 speed at 100 per cent load. Thi?
is obviously not a satisfactory method of operating, particularly at low speeds.
Compensation for the IR drop is obtained in the circuit Fig. 14 in the following manner.
One primary of a current transformer which has two electrically separate primary
windings is connected in each of the two thyratron rectifier-tube anode circuits. The
secondary of this current transformer is connected to the rectifier tube 6. A d-c voltage
which is proportional to the armature load current therefore appears across potentiometer
2P1 resistance 11 R, and potentiometer 3F. The polarity of the voltage across potentiom-
eter 3P is shown. Assume now that the motor is running at no load at any desired speed
and that the Z-R-compensation potentiometer 3P is turned clockwise. Since no armature
current is flowing there is no voltage across potentiometer 3P and therefore the voltage
from 22 to 7 is proportional only to the armature voltage. Now, if motor load is applied,
- Mne 26 will become more negative than line 7. As a result the grid of tube 4 will also
become more negative. This change in grid voltage acts through the amplifier to apply
D-C MOTOR CONTROL
21-29
more armature voltage. The armature voltage is thus raised to compensate for the
resistance drop in the motor due to load. Potentiometer 3P can be adjusted to compen-
sate for the resistance drop in different motors and therefore to hold the speed constant
with load changes. Capacitor 2C is used to filter the rectifier output voltage.
The current transformer and rectifier circuit also provide a voltage signal to prevent
overcurrent which would result in exceeding the rated peak current of the power tubes,
the commutating limit of the motor, and perhaps the torque limit of the driven load.
FIG. 15. Pictorial Elements of Electronically Controlled D-c Motor Drive (Courtesy General Electric
Co.)
Assume that the speed control is set at a high-speed point and the motor-armature con-
tactor M is closed. Tubes 4 and 3 will now control the thyratron rectifiers to give full
voltage output. This voltage would result in approximately 10 times normal armature
current at the first instant. The voltage between points 7 and 11 is proportional to the
armature current. If the armature current is below a normal value (approximately 150
per cent of full-load current) , the grid of tube 5 will be negative with respect to the cathode.
If, however, it exceeds a normal value, the grid of tube 5 will become less negative and the
plate current in tube 5 will control the output voltage of the rectifier (in the same manner
as tube 4 does) to hold the accelerating current at a predetermined maximum value.
When the armature contactor M is open, the rectifier output voltage is still controlled
by the speed-control potentiometer. If the speed-control slider were set for a high-speed
position there would still be an initial high current impulse when the armature contactor
first closed. To prevent this condition a voltage divider consisting of resistors 7R, 8R,
and 9JS is connected across the regulated d-c voltage. Also the rectifier output voltage is
connected to the divider at point 24. When the armature circuit is open, the normally
closed interlock on M connects points 45 to 11. Now, as the rectifier voltage is increased,
21-30
ELECTRONIC CONTROL EQUIPMENT
tube 5 draws plate current which holds the rectifier output voltage at a level which will
result in approximately normal armature current and therefore normal motor torque at
the instant the armature contactor is closed.
Many other features can be obtained by circuit variations. Some common variations
are: (1) control of the motor-field voltage by thyratron rectifiers; (2) control of motor- or
generator-field current; (3) more accurate speed control by means of a small permanent-
PIG. 16. Electronic Motor- and Generator-field Control for Rubber Calender Drive (Courtesy General
Electric Co.)
magnet-type d-c generator mounted on the motor shaft and used as a speed signal; (4)
reversing by current-limit regenerative means; (5) speed programming; (6) timed accelera-
tion in lieu of current-limit acceleration; (7) motor-speed control in accordance with ex-
ternal signals.
Figure 16 shows a control panel for a rubber-mill calender drive which includes electronic
control of the fields of a generator and a 125-hp motor.
14. SIDE-REGISTER POSITIONING CONTROL
Servomechanism is a term often applied to the general field of follow-up or positioning
Side-register positioning control is one of the many examples of positioning
SIDE-EEGISTEE POSITIONING CONTROL
21-31
control which could be selected from this broad, general field. Side-register control is
applied to steel-mill "cotters," to papermill "reels," and to textile-mill "beams" to obtain a
smooth surface at the edge of the finished-material roll. It is also used on slitters for
insulating tape, linoleum, and the like to guide material going from a reel into the slitting
knives so that only a certain amount of undesired edge will be trimmed, with a minimum
of waste beyond the slitter.
One frequent use is an electronic side-register positioning control applied to a paper
slitter. In this application it is desirable to hold the edge of the material at a given point
with respect to the slitting knives. A photoelectric scanner, including a light source, a
phototube, and a preamplifier, is focused on the edge of the paper. The photoelectric
preamplifier supplies a signal to the electronic control panel, which in turn operates an
alignment motor to move a large roll of paper, as well as the nip roll, back or forward in
order to obtain a fixed position of the edge of the paper. Different types of side-register
positioning-control equipment are available to suit varying requirements, such as variation
in contrast between the material and its background, range of colors to be used, alignment-
motor horsepower, accuracy of positioning, and maximum correction rate required.
The circuit diagram shown in Fig. 17 is that of a simple on-off type control. This con-
trol with its associated reversible a-c motor and mechanical brake will meet the require-
ments of applications where: (1) there is a reasonably large light contrast between the
2CR,
10H
FIG. 17. On-off Type Photoelectric Side-register Positioning-control Circuit
material to be positioned and its background or where direct light transmission can be
used; (2) the required accuracy is not greater than plus or minus Vie in.; (3) the required
rate of correction is not greater than 5 in. per min. The correction motor in this case
is a reversible a-c motor which is operated in the forward or reverse direction by magnetic
contactors, which are in turn operated by relays ICR and 2CR. If there is no light shining
on the phototube, the grid of tube 1 will be negative. If tube 1 is not drawing current,
the cathode will go slightly negative, but, in doing so, since the cathode of tube 2 is con-
nected to the cathode of tube 1, tube 2 will be turned on. The lack of current in tube 1
will cause tube 4 to conduct and energize relay \CR. Since tube 2 is conducting, tube 5
will be non-conducting and relay 2CR will be de-energized. If a large amount of light is
now applied on the phototube, the grid of tube 1 will be positive and tube 2 will conse-
quently be turned off. This will result in the opposite operation of relays ICR and 2CR.
The light-intensity adjustment can be turned clockwise to decrease the intensity that
will cause the relays to operate. For a given light intensity, the centering adjustment will
make the transition in the relays occur when approximately half of the light beam is
intercepted or reflected, depending on the method of light transmission. It is obvious
that, if there were no dead zone between the operation of the two control relays, the equip-
ment would be continually hunting from one side to the other. The dead-zone adjustment
provides an adjustable amount of distance over which the material can travel without
actuating the control relays.
In applications where continuous operation of the correcting motor is desirable, the
system just described is not suitable because of the maintenance of the mechanical parts.
In these applications the photoelectric amplifier can control two half-wave thyratron rec-
tifiers which are connected in inverse parallel to operate a shunt-wound d-c motor in the
forward or reverse direction. For correcting motors of 3/4 hp or larger, vacuum tubes are
21-32
ELECTRONIC CONTROL EQUIPMENT
generally used to operate the field of a pilot generator which will in turn supply power to
operate the correcting motor in the forward or reverse direction. Where wide ranges of
light intensities and small light differentials are to be encountered, a more elaborate con-
trol equipment involving a rotary-lens-type scanning head is often used.
15. PROCESS CONTROLS
Electronic control has recently made its way into the field of process instrumentation
and control, where it is now frequently used in measuring, recording, and controlling such
process variables as temperature, pressure, flow, pH, moisture, and the like. An electronic
control unit included. as a part of a complete potentiometer controller is shown semi-
schematically in Fig. 18. The battery supplies a standard reference voltage to the slide
SLIDE WIRE (E)
TEMPERATURE SCALE (F)
CONVERTER
BATTERY / *
THERMOCOUPLE
A. C. LINE
FIG. 18. Semischematic Diagram of Continuous-balance Potentiometer Controller (Courtesy Brown
Instrument Co.)
wire. The voltage produced by the thermocouple is compared with the voltage at the
slider. Since the voltage magnitudes are so small, however, it is not suitable to apply this
voltage difference directly to a d-c amplifier. Instead, it is connected to a vibrating-type
inverter which is synchronized with the power-supply frequency to produce a-c voltage
impulses of a given phase relation in the amplifier tubes. If a difference exists between the
thermocouple voltage and the voltage of the standard, this signal is amplified by an a-c
voltage amplifier and further by means of vacuum-type power-amplifier tubes to control
the power applied to a small reversible-type a-c balancing motor. The reversible balancing
motor repositions the slider until the thermocouple voltage matches that of the battery.
Thus, the pointer is positioned to show the temperature which exists at the thermocouple
location.
If pressure is to be measured or controlled, the pressure-sensitive element can be a
variable reactance. This can be used in an a-c bridge circuit, and the mechanical inverter
is not necessary.
16. SYSTEM STABILIZATION
In any electromechanical system there is a time lag between the application of a correc-
tion signal and the final corrected value; for example: (1) if a given voltage is applied to the
field of a generator, the inductance of the field prevents the field current and therefore the
generator output voltage from building up instantaneously;- (2> if a given voltage is applied
to the armature of a d-c motor the mechanical inertia prevents the motor speed from instan-
taneously reaching its new- value; (3) if a correction voltage is applied to the correcting
motor of a servomechanism positioning control not only must the correcting motor accel-
erate its own inertia plus the inertia of the connected load but it must also run at rated
speed until the new position is reached — then it must decelerate.
SYSTEM STABILIZATION
21-33
Assume that a sensitive and instantaneously operating electronic voltage regulator is
applied to a d-c generator. If the generator output voltage is lower than that called for
by the voltage-adjusting potentiometer, the regulator will immediately apply the maximum
field voltage to attempt to correct the output voltage. The output voltage, however, will
increase slowly because of the field inductance. However, when the output voltage reaches
the desired value the electronic regula-
tor immediately applies the correct field
voltage to hold the desired output volt-
age. Such a system may be slow in re-
sponse, but it is stable in its operation.
If on the other hand it is assumed that
the electronic regulator has internally an
inherent time lag, the operation of the
entire system will be quite different. If
the generator voltage is low, the regu-
lator will again apply maximum field
voltage. When the generator voltage
reaches the desired point, the regulator
will not immediately apply the correct
field voltage because of the inherent
time lag in the regulator. The correct
field voltage will not be established until
Method of Adding a Predominant Time Lag
to Eeduce System Hunting
the output voltage has exceeded the FIG. 19.
desired value. Now, however, the regu-
lator receives a signal which will result
in a weaker field than normal. As a result, the system may be unstable and continue to
oscillate above and below the desired voltage level.
The frequency of oscillation or hunting is determined by the time constants of a system.
If long time constants are involved, the hunting will be at a low frequency; if short time
constants are involved, the hunting will be at a high frequency. In order for hunting to
exist in any system, two conditions must exist: (1) the total time lags of the entire regulat-
ing system must result in the regulating-voltage signal being fed back to the regulator
input 180° out of phase with the normal sense of the correction voltage; (2) at the fre-
quency at which the total time lags
add up to 180°, the overall system
amplification must be equal to or
greater than 1.
Obviously hunting is undesirable in
most systems. Therefore means must
be established to eliminate it. Several
methods are in common use.
As was pointed out earlier, a system
with a single time constant will not
hunt. (Although this is true in general
there are single-lag systems which will
hunt.) Hunting in a system having
two or more independent time lags can
be reduced by artificially adding a time
constant which is sufficiently greater
than the others that it predominates.
Such a system will approach a single-
lag system in performance. Figure 19
shows how a lag can be added to a
d-c amplifier circuit. The grid-to-
plate capacitor charges or discharges
through the series grid resistor at a
rate dependent on the circuit con-
stants. The action of the grid there-
fore lags behind the input signal.
FIG. 20. Method of Adding a Derivative or Rate-of-
change Signal to Reduce System Hunting
Since the overall amplification of the system must be at least 1 at the hunting frequency,
a simple way of reducing hunting is to reduce the system amplification. Conversely, the
higher the system amplification is, the more likely the system is to hunt.
Often rate of change or derivative signals may be added to the input signal to reduce
hunting. Figure 20 shows a typical circuit used in a speed regulator. The steady-state
grid- voltage signal from the tachometer-generator which is connected to the motor shaft
21-34 ELECTRONIC CONTROL EQUIPMENT
is determined by resistors 2R and 3R. During a change in speed, however, the capacitor C
supplies a grid voltage which is proportional to the rate of change of speed and thus pro-
vides a grid signal which is ahead in time relation to the speed signal.
Rigorous solutions to stability problems are often complex. Furthermore, assumptions
of system constants or simplifying assumptions often are proved to be in error when equip-
ment is installed. As a result most systems are stabilized by empirical methods.
BIBLIOGRAPHY
Chin, P. T., and E. E. Moyer, Principles of Grid Control for Thyratrons, A.I.E.E. Technical Paper
45-62 (January 1945).
Chin, P. T., and E. E. Moyer, A Graphical Analysis of the Voltage and Current Wave Forms of Con-
trolled Rectifier Circuits, Electrical Engineering, July 1944.
Chute, G. M., Electronics in Industry, McGraw-Hill (1946).
Chute, G. M., Fundamentals of Industrial Electronics, Steel, April 3-May 22, 1944.
Chute, G. M., Resistance Welding Control, McGraw-Hill.
Cockrell, W. D., Grid Control of Gas Filled Tubes, Electronics, June 1944.
CockreU, W. D., Industrial Electronic Control, McGraw-Hill (1944).
Cooper, B., Better Welds through Regulated Welding Current, Welding Journal, January 1944.
Dalton, B. J., Electronic Motor Control, Proceedings of National Electronics Conference, 1944.
Dalton, B. JM Electronic Motor Control, Gen. Elec. Rev,, May 1945.
DeBlieux, E. V., Characteristics, Design and Application of Rectifier Transformers, Gen. Elec. Rev.,
October, November, December 1937.
Hall, James H., Transformer Calculations for Selenium Rectifier Applications, Electrical Manufacturing,
February 1946.
Hazen, H. L., Theory of Servo-Mechanisms, Journal of the Franklin Institute, September 1943.
Kloeffler, R. G., Principle* of Electronics, Wiley (1942).
Leigh, H. HM and H. L. Palmer, Inverter Action on Reversing of Thyratron Motor Control, Electrical
Engineering, April 1944.
M. I. T. Staff, Applied Electronics, McGraw-Hill.
Moyer, E. E., Electronic Control of D-c Motors, Electronics, May, June, July, September, October 1943.
Palmer, H. L., M. E. Bivens, and S. A. Clark, Electronic Welding Control, Electronics, August, Septem-
ber, October 1943.
Reich, H. J., Theory and Applications of Electron Tubes, McGraw-Hill (1939).
Smith, E. S., Automatic Control Engineering, McGraw-Hill (1944).
SECTION 22
AIDS TO NAVIGATION
RADIO AIDS TO AIR NAVIGATION
ART. BY HENRY I. MUTZ PAGE
1. Introduction 04
2. Terminology and Definitions 05
3. Radio Aids in the Federal Airways Sys-
tem Today 06
4. Facilities in the New Federal Airways
System 13
5. Proposed New Landing Systems 26
6. Proposed New Short-range Navigation
Systems 28
7. Proposed New Long-range Navigation
^ Systems 31
AST. PAGE
8. Miscellaneous Radio Aids 31
RADIO AIDS TO MARINE NAVIGATION
BY M. K. GOLDSTEIN :
' 9. Established Navigational Aids 36
10. Recently Introduced Navigational Aids. 44
11. Contemplated and Proposed Naviga-
tional Aids 63
12. Determination of Optimum Transmis-
sion Parameters for Some Long-range
Radio Navigation Systems 57
22-01
FIG. 1. The Present 35,000 Miles of Federal and Civil Airways. The airway
22-02
CIVIL AIRWAYS. AIRWAY TRAFFIC CONTROL
AREAS. AND FLIGHT ADVISORY AREAS OF
THE UNITED STATES AND CANADA
DATE: JULY 1. IMS
CIVIL AERONAUTICS ADMINISTRATION
DEPARTMENT OP COMMERCE
WASHINGTON. CX C.
rUfflJT LEVELS
max AND «o aw. «*»ws
MTMUNO 000 THOUSAND FOOT U«t*
WESTBOUND EVEN THOUSWD FOOT LEVBS
AM MR ANO BLUE OTl. MKWAYS
NORTHBOUND 000 THOUSWD fOOT LEVCU
KMIHiOUNO-iyO« TMOUSMIO TOOT lEVtti
traffic control boundaries and centers are also shown. (Courtesy CAA.)
22-03
AIDS TO NAVIGATION
RADIO AIDS TO AIR NAVIGATION
By Henry I. Metz
1. INTRODUCTION
Thirty-five thousand miles of federal airways exist today in the airspace over the United
States. This mileage, shown in Fig. 1, is constantly and very rapidly increasing. Informa-
tion about the condition of the airway, weather ahead, and other traffic is available con-
stantly to the pilot by means of
automatic radio aids to naviga-
tion and two-way radio voice
communications.
The establishment, operation,
and maintenance of the airways
are among the functions of the
Civil Aeronautics Administration
(CAA) under the U. S. Depart-
ment of Commerce.
When the federal airways pro-
gram was started in 1926, the de-
velopment of a reliable radio
communication and guidance sys-
tem was undertaken. Basically,
tracks were established in the air-
Fro. 2 (a) . View of Aircraft Automatic Direction Finder Equip-
ment Snowing the Loop Antenna (Courtesy Bendix Aviation
Corporation)
space by overlapping keyed radio
patterns, the points of overlap
being interpreted aurally by the
pilot, who wears a pair of headphones. Although originally produced by a pair of crossed
loop antennas, the tracks are today made by an Adcock array of vertical radiators which
give greater night-time stability. The transmitting station is called a "radio range station."
It produces four tracks called "courses," all of
wnich emanate radially in predetermined fixed
directions. There are 399 range stations now in
operation. The coordinated alignment of a series
of range courses constitutes an airway.
A system of markers has been added to the
range courses. "These are vertically directed
signals at 75 Me, received on a special receiver
in the airplane and connected to a signal light
on the instrument panel. The light operates
only when the airplane is over the marker
station.
An automatic direction finder (ADF), as
shown in Fig. 2, is carried today by most com-
mercial airplanes and is required (in some form)
by CAA on scheduled airliners. Its pointer indi-
cates the direction to the station tuned in. It
may be used as an aid in flying the range course
or to determine position by taking bearings on
two or more stations.
Countries other than United States, Canada, ing
and Australia have based their traffic opera-
tions on ground station direction finding (DF). DF stations are available in these
countries to give bearings to the aircraft calling, just as is now done in locating position
on ships at sea.
22-04
FIG. 2(&). View of Aircraft Automatic Di-
rection Finder Equipment Showing the Bear-
Indicator (Courtesy Bendix Aviation
Corporation)
TERMINOLOGY AND DEFINITIONS 22-05
Airborne direction finders have also been used extensively in other countries in coopera-
tion with high-powered, non-directional, transmitting stations on the ground. A system
called "radio-phare" has been employed in which three spaced ground stations transmit
in time sequence on the same frequency. Without readjustment of the airborne ADF
receiver, three bearings can be quickly obtained from the radio-phare. The German 33-
Mc "Lorenz" instrument landing system (localizer, glide path, and markers), in particular
the localizer, was in quite general use before the war. Its localizer, using interlocked aural
dots and dashes (similar to the U. S. Aural AN Radio Range) to differentiate left from right
in approaching the runway, was used for distances up to 100 miles in cases where the
fixed course alignment agreed with the desired flight direction.
The CAA is engaged in a program of converting all the federal airways aids to static-free
VHF, except that a few strategically located low-frequency range stations will be retained
(with increased power) to serve for long cross-country nights. In addition to converting
to VHF, all future ranges will be of the "visual" type (i.e., using pointer instruments
instead of headphones), and will have omnidirectional courses (i.e., instead of only four
range courses, the pilot may select any radial track, or course, from the station) to take
care of increased numbers of airplanes and airports. Instrument landing systems, de-
veloped previously and now installed at 110 airports, will be used at once to relieve airport
traffic congestion in bad weather. Radar will be used soon as a traffic surveillance device
and, perhaps later, as a direct means of controlling traffic. Pulse techniques will probably
be applied immediately in new meter-type distance-measuring equipment (DME) and
later in anticollision devices. Long-distance nights across water will be guided by rela-
tively low-frequency aids such as omnidirectional, Loran, Sonne, or other systems.
Automatic flight, controlled by radio signals transmitted from the ground, has already
been demonstrated to be more accurate than human-pilot-controlled flight. It will un-
doubtedly be used by all commercial aircraft in conjunction with automatic computers,
to permit controlled, track-type flying in any direction regardless of station position.
2. TERMINOLOGY AND DEFINITIONS
Certain terms associated with radio aids to air navigation in engineering discussions
are listed below with their definitions:
Radio Range. Any CW radio station whose radiation inherently produces directional
courses, or tracks, fixed in their relation to the earth's surface and independent of aircraft
heading. A radar range is similar but uses pulse radiation.
Marker. Any station having limited or directed radiation used to give an aircraft its
position along a range course.
Heading. Direction (azimuthal and clockwise from north) in which aircraft is point-
ing. It agrees with direction of flight if there is no crosswind.
Bearing. Azimuthal angle (from north, clockwise) of line between fixed ground station
and airplane, or vice versa. It is generally necessary to state where the bearing is from
and to, in order to avoid ambiguity.
Track. Actual direction of motion of aircraft with respect to earth's surface, expressed
in degrees of azimuth (from north) .
Beacon, Non-directional. A radio transmitting station whose radiation is essentially
uniform in all directions or which does not use directional radiation characteristics to con-
vey intelligence.
Beacon, Omnidirectional. A beacon whose directional or other radiation characteristics
cause it to give information equally in all directions.
Course Sharpness. The relation between angular displacement from course and deflec-
tion of the pointer of the indicating instrument, usually expressed in angular degrees of
displacement required to give full-scale-left to full-scale-right pointer movement. This
sharpness is generally a function of ground-station pattern sharpness and receiver gain
setting. Localizers are generally used with 4° to 5° sharpness.
Pattern Sharpness. The difference in pattern amplitudes at a given angular displace-
ment from the equal or on-course line, usually expressed in decibels per 1.5°. Standard
figure-of-eight patterns (LF aural ranges) give 0.45 db per 1.5°. The CAA localizer
patterns give about 5 db sharpness.
Clearance. The db difference in patterns producing a course, at angles other than
those containing the on-course. High clearance is desirable so that the indicator will
remain fully deflected everywhere except at the course.
Multiples. Extra or abnormal courses resulting from zero or negative pattern clearance
or from severe reflection of signal from buildings, trees, etc.
22-06 AIDS TO NAVIGATION
Bends. Angular deviation or distortion of the on-course signal from a true, straight
radial line from the station. Generally, bends are produced by reflection of the signal
from buildings or wires near the transmitting station. Bend magnitude is proportional
to the ratio of reflected signal to direct signal amplitude and inversely proportional to
pattern sharpness. Apparent bends can be caused by poor receiver AVC action, allowing
inferior circuit components to unbalance as signal strength changes with distance.
Scalloping. The irregular or wavy shape of an antenna field pattern caused by reflec-
tion of the signal from ground objects. Scalloping is evidenced by the periodic hesitation
in the course indicator movement as the airplane is flown across the course. Scalloping
indicates bends when it occurs near the on-course line. When scalloping is severe, multiple
courses are produced.
Wiggles. Rapid, random, and erratic movement of the course-indicating pointer,
generally caused by combined signal from several reflecting objects, especially trees. Poor
electrical connections and noise also cause wiggles. Wiggles generally do not alter the
average course line and can therefore be filtered out of the indicator.
Pushing (or pulling). Displacement of indicated course with heading of airplane.
Term is derived from observation in cross-course flights that the course was apparently
"pushed" ahead of the airplane. Pushing is caused by the radiation of impure polarization
(vertical in a horizontally polarized system, and vice versa) . Attitude effect, in which the
indicator shifts with airplane roll, or pitch, is similar in cause to pushing.
Distance Range. Distance in miles from the station at which useful signal is lost, or
where course sharpness decreases (loss of AVC). For VHF and above, the line of sight
range generally prevails.
3. RADIO AIDS IN THE FEDERAL AIRWAYS SYSTEM TODAY
The present system consists of the following facilities or services :
A. Radio ranges, LF (four-course aural with simultaneous voice) .
B. Radio ranges (visual two-course, VHF).
C. Radio markers (75 Me).
D. Automatic direction finder (ADF) receivers.
E. Communications (HF and VHF).
F. Air traffic control and weather reporting.
Each of these is explained separately below.
RADIO RANGES, LF (four-course aural with simultaneous voice). The radio range
of today is a 400-watt, highly developed, four-course facility on which practically all civil
air navigation is based. It is notr a perfect device but is simple and effective for distance
ranges up to several hundred miles. Its irregularities are so well known that many of
them appear to the trained pilot as an asset. The change in conductivity of the earth
along the course, in some places, usually in mountainous terrain, causes bends and multiple
courses to appear. The location of these multiples is known and is plotted on charts.
Night effect, which is variable, has been minimized by the replacement of loop-type
transmitting stations with Adcock vertical tower systems. Two highly important objec-
tions to the range are (1) interference by atmospheric and precipitation static, and (2)
interference from other stations in the allotted frequency spectrum.
The present four-course Adcock antenna system consists of five steel towers about 130
ft high. Four towers are placed on the corners of a square; diagonally opposite towers
constitute a pair and are about 600 ft apart. The fifth tower is at the center. The pairs
are connected, but with reversed phase, so that they, respectively, radiate figure-of-eight
horizontal patterns. The two pairs are connected to a crystal-controlled transmitter
through the equivalent of a single-pole, double-throw relay called a "link circuit relay."
The relay is operated by a motor-driven keyer unit so that one pair of towers gives a
series of dot-dash (A in code) characters. The back contact of the relay causes the recip-
rocal character, dash-dot (N in code) to be keyed into the other pair of towers. The
schematic diagram is shown in Fig. 3.
The two figure-of-eight patterns thus contain reciprocal or interlocking characters. To
an observer with a receiver in space the character heard would depend on position around
the station. In a position where the patterns overlap, that is, where the A and N patterns
are of equal amplitude, no character would be observable because they are interlocked
and the signal is a steady tone. The patterns and courses are shown in Fig. 4.
Actually, the radiation from the two pairs of towers is unmodulated carrier energy and
therefore inaudible. The center (fifth) tower is connected to a second crystal-controlled
transmitter, but its carrier frequency is 1020 cycles below that used for the diagonal towers.
Consequently, in combination, the receiver produces a 1020 cycle-output resulting from
RADIO AIDS IN FEDERAL AIRWAYS SYSTEM TODAY 22-07
East
West Center North
Goniometer
MIc
: Wire line
I & Strowger
i control
Dual
transmitter
FIG. 3. Schematic Diagram of Four-course Aural LF Radio Range Showing Simultaneous Voice
N
Fan marker
keying.
Fan marker
keying etc.
' A" quadrant
rZ" marker (75 Mcs)
Fan marker
75 Mcs, 3,000 cps
keying etc.
Fan marker
keying etc*
FIG. 4. Patterns and Courses of LF Aural Radio Range Showing Flexibility of Course Displacement
and Position of 75-Me Markers
22-08
AIDS TO NAVIGATION
the beat between the two carriers. In effect, the center tower radiates the carrier and the
receiver is tuned to it. The signal from the side towers constitutes sideband energy. The
power of the side tower transmitter is adjusted to give, 30 per cent of that of the center
tower carrier signal along the course. The remaining 70 per cent carrier is used for trans-
mission of voice modulation. The airborne receiver generally contains a combination
band-pass, band-rejection filter so that the pilot may select voice or range signals without
interaction.
The course of the aural AN range is normally about 3° wide. The width depends upon
headphone level and the pilot's hearing ability. The change from on-course to full off-
course is gradual; that is, a "twilight" zone exists to either side of the course which permits
the pilot to estimate (very approximately) his nearness to the course.
Normally, four courses are produced at right angles to each other. All four courses
may be rotated equally, clockwise or reverse, by turning a goniometer through which the
outside antennas are connected. Or, if other than right-angle courses are required, as
shown in Fig. 4, the relative phase of the current in opposite towers is varied by means of
artificial lines. The total line length between towers is maintained at an optimum value
for maximum phase and current stability. Under optimum line conditions, the detuning
of rain, ice, and snow on one antenna reacts to produce an equal effect on the other an-
tenna, giving greatest stability of courses.
RADIO RANGES (visual two-course, VHF). The development of a two-course VHF
radio range was started in 1928 to overcome the static, congestion, and dangerous quadrant
ambiguity problems existing on the conventional four-course, low-frequency, aural range.
Now several airways are operating (temporarily on the 110-Mc frequency band) with this
type of facility, pending conversion of the entire federal airways to the VHF omnidirec-
tional system.
The complete designation of the two-course range is: "VHF two-course visual radio
range with quadrant identification." This designation signifies particularly that the
quadrant ambiguity of the four-course type has been eliminated. Actually, the quadrant
identification comes through the superposing of two aural courses on the same visual range,
but with these aural courses at right angles to the visual. This facility, therefore, consists
of two visual and two aural courses, as shown in Fig. 5. Normally, the visual course is
FIG. 5. Basic Patterns and Courses for Two-course Visual Range
flown by observing deviation on a left-right meter. The aural signal reverses when flying
the visual course across the station.
The electrical system of the visual courses is identical to that of the runway localizer
described under "Facilities in the New Federal Airways System" in article 4. The aural
courses are laid down as described above in the discussion of aural radio ranges. Requiring
less course sharpness than the localizer, its antenna array consists simply of three horizontal
RADIO AIDS IN FEDERAL AIRWAYS SYSTEM TODAY 22-09
loops for the visual courses and two additional loops for the aural. The central loop serves
for both the aural and visual courses (see Fig. 6) .
A simultaneous voice feature is incorporated in this range facility by modulating the
carrier fed to the center loop with voice. The total modulation capacity of the transmitter
is divided approximately as follows: 90 cps 20 per cent, 150 cps 20 per cent, 1020 cps 10
per cent, voice 40 to 50 per cent.
The sharpness of the visual course is dependent upon the transmitted pattern shape
and the signal voltages delivered to the receiver indicating circuit. In practice, the
Visual loops
North South
West
FIG. 6. Diagram of VHF Two-course Visual Radio Range
receiver gain is adjusted to give full scale left to right deflection of the indicator for a 20°
azimuthal displacement of airplane (plus or minus 10° from the course). The aural course
sharpness depends upon the patterns and also the pilot or observer. kOn this range it is
about 2°.
The pilot selects the voice broadcasts or 1020-cps aural signals of this range through
the standard range-voice filter described for the four-course range.
This facility is subject to reflection and propagation phenomena characteristic for 110
Me VHF. Objects near the station, such as wires, buildings, and trees, reflect the signal
and give multiple path transmission to the receiver, causing scalloping of the patterns
and sometimes bends or multiple courses. In a moving airplane the random reflections
of trees causes wiggles in the course indicator. Elevating the antenna system higher to
avoid local reflections destroys the course by introducing low-angle nulls in the vertical
pattern of the system. The conventional counterpoise (35-ft diameter) does not eliminate
the difficulty. Horizontal polarization, originally adopted for its superior performance
in the instrument landing system localizer, aids materially in reducing the reflection
amplitude. Probably this is because of its zero radiation at the horizontal angle.
Single reflecting sources at a site generally give smooth (sinusoidal) deviations of the
course indicator. From a knowledge of the wavelength of the bends and the position
where observed, the direction of the reflection source can be determined approximately
by calculation. Distant hills, unless extremely elevated above the station and observed
by a low-flying airplane, do not cause course difiiculties. Good siting is important. Station
sites must be fairly flat and free of the above reflecting sources for a radius of about 500 ft.
The site should also be high because propagation at these frequencies is line-of-sight
(about 45 miles is realized in an airplane flying 1000 ft above the station elevation). ^
RADIO MARKERS (75 Me). An essential part of navigation is position checking
along the route. The radio range gives only direction, or lateral, guidance. The null, or
"cone" of silence, over each range station (Fig. 7) has been used for years as a means of
22-10
AIDS TO NAVIGATION
Direction of flight
determining "over the range" position. Intersecting radio range legs exist at some places
and are used as "fixes" during flight. Special non-directional, low-power, low-frequency
markers have also been used. The difficulties experienced with all of these may be sum-
marized as follows: (1) unexpected fade-out of signal may be falsely interpreted as the
zone over the station; (2) intersecting range legs are not always received in bad weather;
(3) low-frequency markers have been heard
many miles from their desired area at night.
The development of the positive cone or Z
marker overcame these difficulties.
The Z marker consists of a crystal-con-
trolled, 3000-cps tone-modulated, 75-Mc, 5-
watt, dual-transmitter and an antenna array.
,- _10i u * iji x Ll 'htoff_^j The transmitter is located within the range
te fi °n~7 j"| \J8| ° station and is a dual unit with automatic
/ 1 I V— -"7 m.rb-,. transfer in case of any failure. The antenna
is located between the radio range towers
and fed from the main station building by
+20
+10
-20
-30
-40
1.0
Miles
FIG. 7. Range Station Cone of Silence and 75-Mc
Marker Signal Levels Experienced in Flight over
Range Station at 1000-ft Elevation
transmission line. The array may be con-
sidered as two pairs of horizontal, collinear,
half-wave elements, at 90° to each other, and
excited in phase quadrature. The array is
one-quarter wavelength above a mesh coun-
terpoise. The resulting service from this
marker, when received by a longitudinal
doublet under the airplane, is a circular pattern (Fig. 4) several times larger than the cone
of silence and extending upward above the station about 10,000 ft.
The receiver generally used with these markers is a crystal-controlled, single-frequency,
superheterodyne unit weighing approximately 25 Ib and having a maximum available
sensitivity of about 150 microvolts. Its audio output is filtered and connected so as to
cause lighting of a signal lamp on the airplane instrument panel when marker signal is
received. The audio output is connected to the pilot's headphone circuit. Three different
kinds of indicator circuits are in use at present as shown in Fig. 8. The simplest is that
employing a rectifier and relay, used by the AAF. One white light is connected to the
relay contacts. The CAA and airlines use a receiver with no relays but with three output
Receiver audio
t
Rectifier
A.c. from Vibrator
power supply
(a) Army (&) Western Electric 278
FIG. 8. Marker Receiver Signal Circuits
(c) Bencflx
audio filters and three different-colored signal lamps. The white light, operating from
3000-cycle audio, serves for the airways markers (fan and #). Amber and blue lamps,
operating from 1300 and 400 cycles respectively, are used on the instrument landing system
markers.
Good audio selectivity is achieved by designing the indicator-reactor circuit to operate
at about 0 db and by limiting the receiver audio output electronically to about plus 6 db.
RADIO AIDS IN FEDERAL AIRWAYS SYSTEM TODAY 22-11
Any undesired signal, being able to produce only this limited output, will be inadequate
to operate the lights if attenuated merely 6 db. Only simple filters are required.
The third system uses the audio signal directly to light the signal light. Good filters
are employed. When any desired signal appears at the output, some of it is rectified and
fed back to increase the gain of a controlled amplifier stage. This action gives regenerative
response resembling relay action.
Horizontal half-wave doublet antennas are generally used for receiving marker signals.
They are fastened longitudinally about 6 to 10 in. under the belly of the airplane. Some-
times the same antenna is also coupled to the low-frequency range receiver so as to serve a
dual purpose. Some success has been achieved using a shortened antenna flush with the
airplane skin and having a reflecting sheet inside.
Fan marker transmitting stations are keyed, tone-modulated, 100-watt, 75-Mc, dual
transmitters connected by transmission line to a collinear dipole antenna array above a
mesh counterpoise. Three thousand cycle tone modulation is used, and it is keyed in
groups of dashes to identify the leg of the range on which it is located. The station is
located on or near the center of the range course, usually about 20 miles from the range
station (Fig. 4) . Its antenna is aligned parallel to the range course and is received with
greatest efficiency as the airplane passes over or to either side.
The name "fan" is derived from the shape of the marker field pattern. It is fan-shaped,
as shown in Fig. 9, extending perpendicularly across the airway so as to be received even
6000
6
6
42024
Distance In miles from station
FIG. 9. Typical Dimensions of Airways Fan-type Marker
by aircraft considerably off-course. Its range increases with altitude but is generally
receivable 6 miles. 'off course at 1000 ft elevation.
Most of the 257 fan marker stations now operating have an antenna system using four
collinear half-wave elements equally spaced 180° and carrying equal currents of ^ the same
relative phase. The array is one-quarter wavelength above a mesh counterpoise. Two
minor lobes appear in the radiation pattern in the area directly above the station. A new
array has been developed and is being installed in which the four elements carry currents
in the ratio 1-3-3-1 and are physically spaced 220 electrical degrees. This arrangement
eliminates the minor lobes and results in a dumbbell-shaped pattern in horizontal cross-
section.
AUTOMATIC DIRECTION FINDER (ADF) RECEIVERS. The most popular and
most useful radio receiver today is the ADF receiver (Fig. 2). It is an all-purpose receiver
in the present airways system, providing for the reception of signals from radio ranges,
CAA radio communication statiAis, airport control towers, and airline company offices.
This receiver operates with a loop and a short-wire or vertical sense antenna. The loop
gives accurate directional information as well as being very helpful in reducing the effects
of precipitation and thunderstorm static.
The receiver operates as an ADF by virtue of the introduction of an audio modulation
into the loop antenna RF circuit as shown in Fig. 10. The audio frequency is non-critical
and is usually generated in the receiver at about 48 cps. The loop signal, with its locally
superimposed modulation, is coupled through an RF transformer to the non-directional
antenna circuit and to the IF amplifier circuit.
When the loop axis coincides with the direction of arrival of the radio waves, the loop
contributes no RF signal to the receiver system and consequently none of the 48-cps signal
gets through to the receiver IF amplifier or audio output. When the loop is turned so as
to admit signal, the polarity (relative phase) of the 48-cps audio output with respect to
the original 48-cps oscillator output is dependent upon the direction in which the loop is
turned from its original null. A pair of thyratron tubes in a balanced modulator circuit
compares these phases and through saturable reactors in the loop motor supply circuit
drives the loop back toward the null. The motor and control circuit causes the loop to
"seek" and hold the null position of any station tuned in on the receiver. A selsyn follow-
22-12
AIDS TO NAVIGATION
up system is used to indicate remotely to the pilot the position of the loop. The loop
position indicator is calibrated in degrees (0 to 360) and is called the bearing indicator.
In most installations there is some distortion of the received waves because of the struc-
ture of the airplane. This causes an error in indicated bearing called "quadrantal error."
The error is of fixed amount in given directions, and the amount can be determined by
experiment. Cam systems on the loop shaft are usually employed to compensate for the
error automatically.
Pilots peering
Indicator v
X i
- Indicator
Loop
Receiver
Loop
control
equipment
^Permanently excited
motor winding
FIG. 10. Diagram of ADF Receiver Operation
COMMUNICATIONS (HP AND VHF). All communications in the United States
airways system is by voice. The quality of voice signals received from aircraft, and some-
times that from ground stations, is far below any standard that would be acceptable in
other services. As air traffic increases, there will be increasing need for quality, or for a
different system, to preclude misidentification or misunderstanding of received calls. This
condition is not easily cured. The major cause of poor quality is the enclosing structure
needed around the microphone to exclude the 100-db noise in the present-day airplane
cockpit. The ordinary microphone is overmodulated by this noise, and voice cannot be
superimposed without severe distortion. The aircraft microphone is designed to be rela-
tively insensitive by enclosing it in plastic. High-level voice, obtained by close talking,
is admitted through small holes in the plastic.
Two other microphones are used. One, the "throat microphone," is designed to pick
up vibrations from the throat by being worn on the n^ck. The other is the "lip mic"
operating on the sound-velocity principle. Most of the noise pressures strike both sides
of the armature of this mic and are canceled. By attaching it to the pilot's upper lip,
high-level voice is applied to one side of the mic, causing modulation.
Service
Approximate
Frequency Band
Long-range navigation 70-200 kc
Distress 500, 3105 kc, 121.5 Me
Localizera 108-112 Me
Radio ranges 112-118 Me
Air traffic control 118-122 Me
Airline communications 122—127 Me
Air to ground 127-132 Mo
Glide path 329-335 Me
Distance measuring 960-1215 Me
Radar surveillance 3000 Me band
Precision Radar 9090 Me
FIG. 11. Chart of Proposed Frequencies for Air Navigation and Communication
FACILITIES IN THE NEW FEDERAL AIKWAYS SYSTEM 22-13
Airborne transmitters generally operate in the 3 to 6 Me band and have an output of 5
to 100 watts. The lower-power units are used by itinerant fliers in contacting traffic
control towers. Plans are under way to convert all communications to VHF. Many
ground station equipments at airport towers and airway stations are already installed.
The VHF bands as outlined in Fig. 11 will permit numerous channels of static-free serv-
ice. The aircraft antenna at VHF is more efficient than the short wires currently used,
and consequently reliable service (not beyond line of sight) can be expected with the
same or less transmitter power. All airline and itinerant transmitters are now crystal
controlled. This practice will continue on VHF to insure reliable service.
AIR TRAFFIC CONTROL AND WEATHER REPORTING. The air traffic control
system operated by CAA on the federal airways depends solely on voice communication
between the controller and the pilot, assisted by fan markers and "holding" markers
about which planes orbit until cleared for landing.
Advanced weather information is, of course, essential. Numerous weather stations
now release radio-equipped balloons (radiosondes) to permit study of the upper air regard-
less of visibility conditions. These radio balloons emit coded signals revealing altitude,
humidity, and temperature up to about 50,000 ft altitude. The radio equipment is ex-
pendable but is protected by parachute in its fall to earth; some are picked up and mailed
back for reward. Direction finder and radar tracking of radiosondes has permitted deter-
mination of upper-air velocity and direction.
Two new electronic devices permit automatic measurement and recording of cloud-
ceiling height and horizontal visibility, the "Ceilometer" and "Transmissometer" re-
spectively.
The Ceilometer transmitter uses an extremely sharp vertical beam of high-intensity
pulsing light. The source is a 900-watt mercury arc, striking 120 times per second. At a
short horizontal distance from the transmitter, a photoelectric cell scans the entire beam
from its base to top. If the beam is striking a cloud layer, the reflection will appear in the
cell output. The vertical angle of cell at the time the output is observed is indicative of
the height of the cloud layer. A recording device makes a record of the ceiling altitudes.
A unique feature of Ceilometer is the use of pulsing light to eliminate the otherwise ob-
literating effect of daylight. Daylight, being steady, is filtered out of the system, permit-
ting equally high ceiling measurement performance in daytime as at night.
The Transmissometer, which measures the light transmissivity of the air, is similar to
the Ceilometer in utilizing a concentrated beam of light and a photoelectric cell. In the
Transmissometer, however, the light is steady and directed horizontally to the cell through
a kilometer of air near the airport approach lane. The effect of daylight is removed by
shielding and baffling and by proper choice of beam intensity. The output of the cell is
converted into pulses, the lowest pulses corresponding to low transmissivity. In the
weather bureau these pulses are converted into relative values of direct current for ob-
servation or recording of visibility.
4. FACILITIES IN THE NEW FEDERAL AIRWAYS SYSTEM
The new federal airways system, now being placed in operation, will utilize VHF radio
for ranges, instrument landing, and communications. The adoption of VHF relieves the
troubles of static, both atmospheric and precipitation types.
The new radio ranges will be omnidirectional to satisfy the need for more airways, better
traffic control, and most particularly to give useful navigation information regardless of
position from the range station.
Distance-measuring equipment is planned as an ultimate replacement for fan and Z-
type radio markers. Operating with the omnirange it will provide the basic requirement
for safe air navigation — accurate knowledge of position at all tunes.
Congestion of traffic at air terminals will be reduced by the VHF instrument landing
system now installed and by closer coordination in air traffic control.
In the new system all navigational information will be received visually, that is, by
meter-type presentation. Some use of cathode-ray tubes may result from development
work now under way, especially for anti-collision and air traffic control. Whether the
presentation is by meter or cathode-ray tube, some effects from reflection of signal by
buildings, trees, or mountains near the ground station will exist. These may cause bends,
multiples, or wiggles in the course as indicated by the meter. In radar systems, wherein
all the intelligence is obtained by visual study of the cathode-ray tube, the operator can
generally separate the main from the reflected signal visually. Pulse technique does not
in itself eliminate the effects of reflections, but when displayed against a time base^ on a
cathode-ray tube it permits a study of all signals received. The reflected signals are visibly
displaced and diminished by the extra tune required to travel their longer paths*
22-14
AIDS TO NAVIGATION
INSTRUMENT LANDING SYSTEM (CAA). Instrument approach, or landing by
instrument guidance, is just now being put into practice in the United States. It comprises
a runway localizer, a glide path, and three marker beacons.
FIG. 12.
|90<M|
Alt. Motor Alt.
Diagram of CAA Electronically Modulated Localizer
Localizer. The localizer creates a course, or track, along the center line of the runway,
by overlapping two bean-shaped radio patterns having different modulation frequencies
(90 and 150 cps). The signal service area extends slightly beyond the line of sight, but is
conservatively given as 25 miles at
| 1000 ft (airplane elevation). The fre-
J quency is 110 Me.
The localizer transmitting antenna
array consists of eight horizontally
polarized loops, spaced symmetrically
across the center-line extension of the
runway. It is generally 1500 ft from
the end of the runway and elevated
only about 12 ft. Each of the three
outside loops on one side is paired
electrically with a loop in similar po-
sition on the other side. Each pair is
connected through a control to a com-
mon sideband generator, as shown in
Fig. 12. There is a 180° phase re-
versal in the tie line between the pairs.
The sideband energy is radiated with
a sharp null down along the runway
center line, as in Fig. 13a. The center
two loops are connected in phase
(Fig. 12) to radiate carrier, modulated
with equal amounts of 90- and 150-cps
voltage. The radiation pattern is
shown in Fig. 136. When the side-
bands in patterns a and b of Fig. 13
combine in the receiver and appear
FIG. 13(o). Antenna Pattern of the CAA 8-loop Local- at the filtered output, the_ overlapping
izer. Side-band loops.
patterns of Fig. 13c are obtained.
FACILITIES IN THE NEW FEDERAL AIRWAYS SYSTEM 22-15
The airplane receiver, Fig. 14, is adjusted initially so that its filtered output of separate
90- and 150-cps voltage is well balanced. The output is connected to a balanced rectifier,
and the rectifier is connected to a zero-center microammeter. The meter remains centered
as long as equal amounts of 90- and
150-cps modulation are received, as ^
when flying along the runway center |
line in the sideband antenna null.
Deviation of the airplane right or
left brings it out of the null. The
sideband signal then received adds
to that obtained from, the carrier.
On one side of the null (or course)
the 90-cps signal adds to that of the
carrier while the 150-cps signal sub-
tracts. This causes deflection of the
zero-center meter. The reverse is
true on the opposite side of the
course. The zero-center meter (Fig.
15) is used by the pilot to determine
deviation from and ^direction to the
course. The same instrument usu-
ally contains a second pointer, cen-
tered horizontally to indicate devia-
tion from the glide path. The "U"
receiving antenna is shown in
Fig. 21a.
Although it is possible to obtain
almost unlimited course sharpness
in the localizer course by expanding
the transmitting array and increas-
ing the receiver output level, there
is a maximum that can be used
safely and conveniently by average
pilots. The sharpness will probably be standardized at 5
right, for 2.5° deviation from course).
Only part of the 200-watt carrier (40 per cent) radiated by the center pair of loops is
modulated by the 90/150 cps signals.
S* The balance is used to handle tone
identification keying and control tower
voice modulation. The latter is ex-
pected to be an aid in approach control
of airport traffic.
Glide Path. The glide path is
established by a crystal-controlled
transmitter capable of delivering
about 25 watts at 330 Me to an an-
tenna system producing two types of
lobes. One antenna produces a beam
quite broad in the vertical plane (see
Fig. 16a) which is modulated at 90
cycles. This will be called the upper
beam. The other antenna is modu-
lated at 150 cycles and is raised sev-
eral wavelengths off the ground to
produce a multilobed pattern with
each lobe quite narrow in the vertical
plane. Comparison of the broad up-
per lobe with the lowest of the narrow
lobes establishes the glide path. This
equisignal path is generally about 2.5°,
although adjustment of the heights of
the antennas can bring the crossover
at any angle between 2° and 4°. An
accurate plot of the lobes involved
FIG. 13 (c). Combined Side-band Pattern (a) and (6) for the 2.5° path is shown in Fig. 17.
FIG. 13(6). Antenna Pattern of the CAA 8-loop Local-
izer. Carrier loops.
(deflection to last dot left, or
22-16
AIDS TO NAVIGATION
The separate modulation frequencies are generated by a mechanical modulator consist-
ing of a synchronous (1800-rpm) motor and two metal paddle wheels having three and
five paddles, respectively. The paddles detune associated resonant sections of trans-
mission line coupled to the respective antennas and create 100 per cent modulation at 90
and 150 cps. The modulator is shown in the diagram, Fig. 166.
±2
Fll'ters
Horrzontal pofnteY
used only with ils
glide path receiver
Course
sharpness
control
§< h^/WW ) <
FIG. 14. Localizer Receiver Output Circuit
.Pilot's cross
pointer Instrument
The equisignal surface represented by the two radiations of the station is obviously
conical; paths from all directions terminate at the station. The station had to be placed
off the side of the runway for safety reasons. This means that the approaching airplane,
if in line with the runway, must follow a hyperbolic path whose minimum altitude exists
directly opposite the station. To straighten out the bottom portion a special relation
between the horizontal patterns of the upper and lower antennas had to be applied.
The receiver for the glide path uses a crystal-controlled superheterodyne circuit and a
28-volt d-c supply. It requires no high-voltage dynamotor or vibrator power supply.
cr
o
(6)
FIG. 15. Cross-pointer Instrument with. Flag-alarms to Indicate Signal Failure, (a) Dead needle
position showing alarm flags in position. (6) Operative position with alarm flags behind mask. (Cour-
^ tesy AAF.)
The output audio (90 and 150 cps) is filtered and separately rectified as in the localizer
receiver, Fig. 14. The resultant direct current is connected to a zero-center instrument
(horizontal pointer of cross pointer instrument, Fig. 15). The pilot flies on the path,
keeping the pointer centered, or horizontal. The dipole antenna, shown in Fig. 21a, is
used hi receiving the glide-path signals.
FACILITIES IN THE NEW FEDERAL AIRWAYS SYSTEM 22-17
It is evident in that the glide-path equisignal lines converge and become very sensitive
to vertical displacement of the airplane near the station and runway. This is offset by
designing into the receiver about 9 db of negative AVC. This has the effect of reducing
the receiver audio output voltage as the airplane approaches the station. An additional
Upper ant.
150 ™
Lower ant.
90f\j
Coupled section
Mechanical
modulator
•Transposition
^ntl-cross modulation
bridge
M = motor
L = load balance
90 ru pattern
"(lower ant.)
Ground
(W
V>*/ ^uj
FIG. 16. 333-Mc Straight-line Equisignal Glide Path, (a) The lobes of elevated antennas produce
an equisignal glide path. (6) Modulation is accomplished mechanically with coupled sections.
4-db reduction or "softening" of sharpness is derived by beaming unmodulated carrier
across the path near its bottom end.
Markers. The markers used in instrument landing are, fundamentally, position-
indicating devices similar to the Z markers discussed on p. 22-10. They will be replaced
eventually with accurate distance-measuring devices which continuously indicate mileage
to the runway. The present two markers are identified both aurally and visually by
tone and keying. The outer marker (distance 4.5 miles) is modulated at 400 cps and
keyed in long (2 per second) dashes. The middle marker (distance 3500 ft) is modulated
1
J
&
c
,
x^
^^
X
/
'
\
/
f
ver radiator
(565.3° sin
a)
\
sin
2.5°
path
/
\
16.5°
False path with
reverse sensing
/
.
/ Up
/0.4
62 sir
iator
(268
5° sin
a)
s
^
1
I
r
/
r
^
^
,
s^
\
I
^
1
\
/
\
/
\
/
\
Y
/
/
\
/
\
/
\
/
\
n
\
//
\
/
\
/
\
\/
' i
i
\
L
\
w
V
V
i
D 1 2 3 4 5 6 7 8 9 10 11 12 13 14 15 16 17 1«
Vertical angle a
FIG. 17. Accurate Plot of Radiations Showing Formation of Glide Path
at 1300 cps and is keyed in a series of dot-dash characters. The boundary marker, re-
cently discontinued, was modulated at 3000 cps and was keyed in fast dots (6 per second).
The outer and middle markers are further identified by signal lamp color, purple and am-
ber respectively.
22-18
AIDS TO NAVIGATION
THE OMNIDIRECTIONAL RANGE (VHF). This facility is produced by radiating
simultaneously, from the same antenna array, two signals having the same audio-frequency
modulation but having different relative phase for different azimuthal positions around
the array. One signal is non-directional, and since its phase is everywhere (in azimuth)
the same it is called the "reference phase" or voltage. The second is produced by rotating
a "figure-of-eight" pattern. This pattern produces a modulation in the radio receiver,
the frequency being dependent on the speed of rotation. Since its relative phase varies
with azimuth it is called the "variable phase" or voltage. Since the two frequencies gen-
erated are equal, and a standard relation is set for north, comparison of the relative phase
anywhere will permit determination of azimuth bearing from the station.
A five-loop transmitting array is used, and it is mounted on a tower 15 ft high with a
circular counterpoise. Four loops are installed as diagonally opposite pairs. These are
connected (Fig. 18) to the transmitter through a capacitance goniometer whose rotation
I 30<\> reference
FIG. 18. The CAA VHF Omnidirectional Range System Diagram
at 1800 rpm causes the figure-of-eight space pattern of the loops to rotate in synchronism.
It produces a 30-cps modulation of the carrier in the receiver.
The center antenna is connected directly to the transmitter. The transmitter is modu-
lated by a 30-cps voltage derived from a tone-wheel generator locked on the goniometer
shaft. If the two 30-cps signals in the receiver output are in phase when the plane is north
of the station, the phase difference in degrees elsewhere agrees directly with the degrees in
azimuth of the receiver.
Two 30-cps signals cannot be directly isolated in the transmitter or receiver, so a sub-
carrier of 10 kc must be used for the reference signal. Further isolation is provided by
frequency-modulating the subcarrier with the 30-cps voltage. Both the subcarrier and
its required FM are derived from the tone-wheel pickup by using non-uniform spacing of
teeth on the wheel. A "clipper" (see Fig. 18) is used to remove modulation on the RF
to the goniometer.
The rotating pattern, which is sideband energy, effectively modulates the carrier about
30 per cent. The subcarrier modulation is equivalent to 10 per cent. The remainder of
carrier is utilized for tone-keyed identification and voice communications.
The receiver used is a conventional superheterodyne up to the second detector. Here a
filter is imposed to separate the 10-kc subcarrier and the variable 30-cps modulation. The
10-kc subcarrier is fed to a discriminator from which the reference 30-eps signal is obtained
as illustrated in Fig. 18.
The two 30-cps receiver output signals are connected to a wattmeter circuit. The indi-
cating element of the wattmeter is a zero-center instrument which is used as a course
indicator. When the phase difference between the reference and variable signals delivered
to the circuit is 90°, the indicating instrument will be centered. This may be standardized
as the north, or east, bearings of the station. Varying of the receiving point from this
FACILITIES IN THE NEW FEDERAL AIRWAYS SYSTEM 22-19
bearing will cause movement of the zero-center meter. Full-scale reading is obtained in
the system when the receiving point is displaced 10° from north. A variable phaser,
Fig. 18, is provided to delay, or advance, the one signal before delivery to the wattmeter
Knob
Azimuth
selector
(phaser)
Flag (Signal failure)-
alarm
(a) Circuit for Manual Selection of Omnirange Track
Filter Ampl'. Discriminator I ^ff | Amp!'.
10 kc
Magnetic vane
Automatic & pointer
bearing
Indicator
Audio output
+ B
(6) Circuit for Omnirange Automatic Bearing Indicator
FIG. 19. Aircraft Receiver Output Indicating Circuits
circuit. If sufficient phase change is inserted to center the pointer of the indicating instru-
ment, the amount of phase change inserted is proportional to the azimuth bearing. The
phaser is calibrated 0° to 360°. This phaser setting is taken as the airplane-to-station
bearing when the 'zero-center meter pointer is centered.
Obviously, there- are two positions of the 360° phaser where the indicating instrument
will be centered. This ambiguity is indicated either by a combination of red and green
22-20 AIDS TO NAVIGATION
lights or by a smaller zero-center ambiguity meter. When signal lights are used, they are
operated from a relay which is normally closed for correct signal and open for incorrect,
or insufficient, signal. The relay closing is achieved by combining the two voltages in
phase through an amplifier. Since the voltages are normally equal, reversal of one causes
complete cancellation, the relay releases, and the red light comes on.
The alternative method uses a wattmeter circuit similar to that in the original course
indication; however, its variable signal is shifted 90°. It, therefore, indicates a course 90°
displaced to the true course. The ambiguity meter indicates full scale right until the
airplane passes over the station. At this instant it swings to the opposite side, indicating
that the station has been passed and that the bearing is reciprocal. When the ambiguity
meter centers, it indicates failure of one or both signals or an inoperative receiver. One
such meter is diagrammed in Fig. 19a.
Figure 196 illustrates an automatic "bearing indicator" for the omnirange. Its pointer
follows up the bearing changes made by the airplane, always displaying correct bearing.
It is a magnetic device with crossed coils connected to the respective rectified variable
and reference phases from the receiver. Cathode-ray tube and other types of indicators
have been developed. One system combines the omni- and the gyrosyn-magnetic com-
pass to give the equivalent of VHF ADF.
DISTANCE-MEASURING EQUIPMENT. The distance-measuring equipment with
meter indication depends for its operation on the challenging of a ground "radar trans-
pondor beacon" by an airborne challenger. The challenger is a radio transmitter-receiver
which transmits a pulse-type challenge to and receives a pulse-type reply from an auto-
matic radio receiver-transmitter known as a transponder beacon. The time elapsed
between transmission of the challenge and receipt of the reply is a measure of the distance
between the challenger and the beacon. This time difference may be converted to a d-c
voltage whose magnitude is proportional to distance and can be read on a meter.
The challenge signal consists of a "pair" of RF pulses in the 960-990 Me band so that a
beacon setting must agree with two pulse characteristics before the beacon replies. These
are the challenge frequency and the time separation (called mode) between the two pulses
of a pair. This "frequency-mode" combination is called a challenge channel. The reply
channel consists of a "pair" of RF pulses in the 1185-1215 Me band. Challenge and reply
channels in combination form an "operating channel." The beacon and the challenger
receiver distinguish between pulses intended for them and pulses at the same frequency
but different modes by use of a "decoder." One form of decoding is to delay the first
pulse by an amount equal to the mode and operate only if the delayed pulse is then co-
incident with the second pulse.
An individual plane identifies the replies to its own challenges, as distinguished from
replies of the same beacon to the challenges of other planes, by the fact that its own replies
occur after a fixed (or slowly changing) time (i.e., distance) after its challenge, while the
replies to other planes occur at a random time. The airborne receiver is "gated on" for a
very short time interval at a fixed time (i.e., distance) after each challenge. It is as if the
receiver asked the question, "Is there a reply from a beacon at a distance between 20 and
22 miles?" The gate duration is defined as 22 minus 20 or 2 miles. In one design the gate
is divided into two subgates called (1) the "early gate" and (2) the "late gate." If the
signal occurs in the early gate, the time delay of the gate is decreased for later challenges
(it is gated on at 19 instead of 20 miles). Likewise, if the signal occurs in the late gate,
the time delay is increased for later challenges (it is gated on at 21 instead of 20 miles).
This system of subgates allows automatic following of the signal. The time between the
challenge and the "gate" is translated into volts by a measuring sawtooth voltage which
defines the volt-time (i.e., volt-distance) relationship.
While searching for a beacon, the gate is made to travel slowly over the total distance,
advancing a fraction of its duration after each challenge. It is as if the gate asked the
question, "Is there a reply between 20 and 22 miles?" then after the next challenge it
asked, "Is there a reply between 20.5 and 22.5 miles?" etc. If the gate finds a high enough
percentage of replies to challenges, the search is terminated and tracking begins; that is,
the receiver thereafter holds the signal which has been found.
Each beacon is identified by "gap coding"; i.e., its transmission is interrupted by a
keyer in such a manner that the gaps form a Morse character. Failure to receive a reply
results in lighting a lamp in the cockpit which therefore flashes the beacon's code.
A beacon is disabled for a short time after replying. This time is called ' 'beacon recovery
time" or "beacon dead time." While this "recovery time" may serve many useful purposes
such as preventing over-interrogation, it also results in failure to reply to those challenges
which occur while the beacon is recovering from a previous interrogation. This failure
is called "count-down" and is expressed as the ratio of missed replies to the total number
of challenges.
FACILITIES IN THE NEW FEDERAL AIRWAYS SYSTEM 22-21
The number of aircraft signals that can be handled simultaneously by a given beacon,
is very important. The system described above, through choice of pulse dimensions and
random rate, can handle approximately fifty airplanes per channel simultaneously (sixty
channels are repeated in every 500 mile square) . A block diagram of the airborne unit is
shown in Fig. 20.
Distance can also be measured by the same principle as that employed in the radio
altimeter, but with the aid of ground respondor stations. Continuous-wave frequency-
modulated transmission is employed. The modulation is varied over a cycle which is,
in duration, equal to at least the time required for travel of the signal to and from the
most distant beacon to be measured. The frequency of the received signal at any instant
is different from that then being emitted. The difference is a function of the time and
therefore the distance. The meter-style indicator can be calibrated in miles. The disad-
vantage of this CW system is that it can handle only one aircraft at a time.
Trans-
Mod.
Multivlb.
Linear
sweep
mitter
Mileage
Indicator
(voltmeter^
FIG. 20. Functional Diagram of Distance-measuring Equipment (Airborne Unit)
Audio phase comparison methods have been proposed and tried experimentally. In
this method an audio modulation frequency is chosen whose wave period (360°) is the
same as the time required for transmission to and from the maximum distance to be
measured. The radio signal travels 186 miles in 1 ms. Therefore, a 1000-cps frequency
will shift 360° in 186 miles. If the airplane and ground station are 93 miles apart, the
round trip between them is 186 miles and the 360° shift will prevail as the maximum range
for the 1000-cps wave.
By sharing time through random keying of the airborne transmitters, several aircraft
may obtain separate distance information simultaneously in- the audio phase comparison
system from the same ground station.
AIRCRAFT EQUIPMENT (RECEIVING). Almost universally, aircraft receivers have
been of the superheterodyne type. Tunable receivers have been used generally, with spot
frequency for control towers (278 kc) crystal-controlled or fix-tuned. In the VHP system
the superheterodyne principle is again being universally used. Crystal control is benig
used for most commercial .applications and manual tuning for inexpensive units for itin-
erant fliers. In the crystal-controlled receivers each of the several crystals employed will
produce a multiplicity of receiving channels. Over two hundred channels are needed by
aircraft on routine instrument nights, in the bands illustrated in the national plan, Fig. 11.
Many companies have, or are installing, dual ADF receiving equipments in each air-
plane so that automatic indication, or plotting, of aircraft position can be used. Single
instruments with dual pointers, one for each ADF receiver, and each receiver tuned to a
separate station, are very helpful in navigation. ^
VHF receivers for navigation are equipped to serve all VHF functions required in flagkt.
Two such receivers in an airplane give adequate stand-by protection. In normal use one
is available for communication while the other is being used for navigation or landing.
Two types of output indicating circuits are now used in each of these navigation re-
ceivers. The amplitude comparison type (90-150 cps) will be retained only until existing
localizers of the instrument landing systems are converted from amplitude to piiase
comparison principle. Then the phase comparison type indicating circuit will be used
for both omni navigation and landing. m .
An outstanding advancement in receivers was made during the war in the elimination
of aU receiver high-voltage power supply. Through the development and application of
the 28-volt-type tube (28D7) a complete 330-Mc, superheterodyne, glide path receiver,
using no vibrator or dynamotor-type supply, was produced in quantity. -
22-22 AIDS TO NAVIGATION
volts direct current, available in the airplane, is used as plate supply. An ADF receiver
was developed later, also avoiding the HV supply. The reduction in noise and main-
tenance and the saving in weight by this development are extremely important factors.
Receiving antennas have been an important part of the VHF program. Whip or mast-
type vertical antennas are the best for ease of installation. For lateral guidance functions,
however, horizontal polarization has been declared superior. Suitable antennas are illus-
trated in Fig. 21. The patterns of the U and V antennas are essentially circular, as required
for their navigational function in range and localizer receptions. The 330-Mc dipole on
the U antenna, in Fig. 21, is used for glide path reception. It is required to have only
forward glide path reception during the runway approach procedure.
330 me glide path
110 me localizer
(a)
FIG. 21. Receiving Antenna for the Instrument Landing System, (o) The U is for 110-Mc band
localizers, and the dipole is for the 330-Mc glide path. (6) An experimental V antenna for non-
directional reception of localizer or range signals.
For navigational service, pure polarization is essential in the radiated wave. If polariza-
tion is impure, that is, unintentionally mixed, serious attitude effects are evident in the
indicator when the airplane is banked or turned.
Balanced transmitting and receiving antennas are now used.
AUTOMATIC FLIGHT AND LANDING EQUIPMENT. For automatic navigation,
the new electric auto-pilot has become the greatest asset. With it, straight and level
flight is made by gyroelectric control, or completely coordinated (aerodynamically) turns
of the airplane may be made by turning a knob which simply unbalances electrical bridges
in the auto-pilot system. If the bridge circuit is electrically connected to the output of
the new navigation receiver (localizer or radio range) through an appropriate amplifier
or coupling system, the auto-pilot can be made to fly the airplane accurately along the
localizer or radio range course. Or the output of the receiver (direct current which is
proportional to displacement from the course and whose polarity reverses when crossing
the course) may be made to operate a steering motor right or left, to follow the course.
The steering motor turns the auto-pilot steering potentiometer.
The operation of one type of electrical auto-pilot, and one way in which the radio signal
may be coupled to the auto-pilot, are shown diagrammatically in Fig. 22.
Coupling the radio guiding signal to the auto-pilot and obtaining satisfactory perform-
ance involves consideration of the mass and speed of the airplane, sharpness of the radio
course, and characteristics of the auto-pilot itself. The desired 'performance is that giving
asymptotic approach to the course. In the off-course position, a "displacement" signal
must be applied to turn the airplane right or left as required. The displacement signal is
obtained directly from the radio receiver and is proportional to the angular distance from
the course. Acting alone, this displacement signal would reduce the turn of the airplane
to zero as it crosses the course. But the airplane heading at the time of crossing may be
at any angle to the desired course. The airplane travels to the opposite side of the course
before a reverse signal is applied. The result of displacement signal alone would be a
continuous oscillation of the airplane across the course as it flies toward the guiding radio
station.
In the coupling device, a "rate" signal must be applied — a signal whose amplitude is
proportional to the rate of change of displacement, and whose control on the airplane
through the auto-pilot is reverse from that of the displacement signal. With proper design
for any particular airplane, the rate circuit reverses the turn of the airplane as it nears
the course and causes it to follow the desired asymptotic curve. Because of the converging
sharpness feature of radio courses, a compromise must be made in the coupling system
characteristics. In general, however, good performance has been achieved. On the
final approach to the airport on the localizer, the vertical pointer of the course indicator
seldom deviates from center by more than its own width, regardless of any cross-wind
velocity or direction.
FACILITIES IN THE NEW FEDERAL AIRWAYS SYSTEM 22-23
Flight toward or away from the station is obtained by reversal of connections (polarity)
between the radio receiver and coupling unit. The switch positions are marked "inbound"
and "outbound" respectively.
Very flexible radio range navigation is now possible through the use of computers. For
the federal^ airways system these computers would operate in conjunction with the VHF
omnidirectional range and distance-measuring equipment. With the computer, it is
D c signals from locallzer
Cross pointer
nstrument
Vibrator
400rul
• — --'ill
Jrr\
D-c signals from
It-fir
v y-
To sim
coupling
for thrc
or elev
— /
ar
unit
ttle
ator
\1JJ
DC 1
DC -nf
Smoothing
Rate derivation
Conversion dc to ac
— *vWv>--f- *•— jfn
Ac
Conversion of a-c p^H
signal amplitude Fbeaecdk"
Into equivalent
mechanical rotation
nc
Ac
Preamplifier
"t-
i
If
Servo
amplifier
Anti-
hunt
I I
Servo motor
& gear box
Vetoc.
gen.
$
400 <\J
Conversion of
mechanical
rotation Into
auto-pilot signal
Auto-pilot
system
Bank limit adj.
40000
FIG. 22. Auto-pilot and Radio Coupling Systems
possible to fly a synthetic left-right indicated course in any direction, whereas the regular
courses are defined only toward or away (radially) from the station.
Referring to Fig. 23, S represents the omnirange station, and the course to be flown lies
along the non-radial line AB. The distance-measuring equipment (described above)
produces a voltage ei which is proportional to r, the distance to the airplane. This is
applied to a selsyn primary (rotor) which is connected to the omnirange azimuth indicator.
The sinusoidal output of the selsyn secondary winding is
62 — ei sin 9
because it is designed to vary sinusoidally with rotor angular displacement. Since ei is
proportional to r, the equation may be written:
62 = &r sin 6 = ky
The voltage eg therefore is proportional to the variation in y, that is to the displacement
of the airplane from the line AB. This displacement voltage may be balanced by a fixed
voltage and presented on the usual left-right course indicator for manual flight, or it may
be coupled to the auto-pilot for automatic flight along the selected line AB.
22-24
AIDS TO NAVIGATION
In setting the computer so that the constant k will be properly handled, the course line
to be flown is decided upon and drawn on the range map. The direction and length
of the perpendicular from the range station to this line are determined. The direction of
the perpendicular is set into a calibrated clutch between the azimuth indicator and the
selsyn unit. The length of the perpendicular line is set up on the "lane selector" switch,
thereby providing the required fixed balancing voltage. Then the pilot's left-right indica-
tor will be centered only when the airplane is on the desired flight line.
Azimuth /
clutch v^,,/
Dtrectlor
(0)
indicator
For automatic
flight control
FIG. 23. Computer for Synthetic (r0) Courses
RADAR MONITOR FOR AIRPORT TRAFFIC CONTROL. Civilian aviation will
require the use of radar as a monitor in airport control towers. Development of suitable
equipments is under way. Its first use will probably be in expediting the outbound traffic
at the congested terminals. The airport tower operator, having accurate knowledge of
the displacement of all inbound airplanes, through reference to the radar monitor, may
permit the departure of airplanes that otherwise would be required to await position reports
from the inbound airplanes.
Three fundamental problems are evident in the application of radar to airport control
towers. These problems are typical of all civil radar application. They were overcome
in military use by a multiplicity of radar equipments and large operating crews. The
problems are: (1) reliable coverage up to about 30 miles, from horizon to zenith; (2) the
elimination of undesirable ground clutter; (3) the presentation of resulting radar informa-
tion in a manner such that the regular tower crew can use it safely, at any instant day or
night, without special enclosures.
Relatively high-angle coverage has been obtained by means of antennas giving cosecant-
squared patterns, shown in Fig. 24. When the energy is distributed in the required pat-
tern, the maximum distance range is naturally reduced. A peak power output of about
0.5 megawatt is required to give the 30-mile horizontal coverage with a cosecant-squared
.pattern.
. Some work has been done on the elimination of ground clutter as illustrated in Fig. 25.
Only moving targets are permitted to appear. Development is being continued to sim-
plify the equipment and reduce the maintenance required to keep it in perfect adjustment.
FACILITIES IN THE NEW FEDERAL AIRWAYS SYSTEM 22-25
The presentation feature has not yet been satisfactorily solved. New, high-intensity
cathode-ray tubes are being made available as an aid to the daylight presentation prob-
lem. Another means of getting the radar scope picture visible in daylight is comple-
12 3 456 78 9 10 11 12 13 14 15 16 17 18 19 20
Distance In miles
FIG. 24. Cosecant-squared Pattern of GCA Search. Antenna
mentary light niters. For example, if the control tower window glass is colored blue and
an amber filter is used over the face of the radar scope, the picture will appear the same
as at night. The reflections of the observer's face can. be eliminated by installing the amber
filter at a 45° angle.
FIG 25 Radar 10-mile PPI Scope Pictures, (a) Heavy ground clutter from objects surrounding'the
station "at the Indianapolis Airport. The targets between 60° and 100° are buildings in Indianapolis.
22-26
AIDS TO NAVIGATION
FIG. 25.
(6) Same as (a) except that Ground Clutter Is Removed and Four Airplanes Are Shown in
Plan Position (Courtesy CAA)
5. PROPOSED NEW LANDING SYSTEMS
GROUND CONTROLLED APPROACH (GCA). At the beginning of the war, a
talk-down system was conceived for landing airplanes in bad weather. It became known
as GCA because it served in reverse to other systems — it controlled from the ground.
Several sets of GCA were put in service before the end of the war. Many sensational
landings of military airplanes were made with GCA, saving lives and valuable property.
Its use required no new airborne equipment but depended only upon communications and
a cooperative pilot.
The GCA equipment is a composite, trailer-type station with three radar systems and
complete communications equipment. It is placed about 500 ft to the side of the runway
and at the end opposite from that on which the landing is to be made. Air-conditioning
and power-generating equipment are carried on the towing truck.
Originally the GCA trailer required a crew of five operators. Four of them constantly
watched four radar scopes, and the fifth served as final approach controller to give heading
and rate-of-descent instructions to the pilot on the final approach. Now, however, the
operation of landing a single airplane may be handled by one operator who shifts his
attention from search to precision scopes as the airplane orients and approaches the run-
way, Fig. 26. If more than one airplane is involved, more operators are required.
The function of GCA, whether operated by one or more men, is as follows : (a) search for
aircraft in all directions, using PPI scope presentation; (fe) direct aircraft into the landing
sector about 6 miles from the runway at 1500 ft elevation, on the basis of search radar
PROPOSED NEW LANDING SYSTEMS
22-27
information; (c) land the airplane by giving the pilot explicit instructions constantly
during the approach as to heading and rate of descent, on the basis of precision azimuth
and elevation radar information.
The search function in GCA is obtained at 10 cm by an antenna rotating at 30 rpm. The
antenna is a special reflector with bvo-dipole array fed by rectangular wave guide. Its
radiation pattern is illustrated in Fi£. 24.
The precision radar system consists of one transmitter (3 cm) sharing time with two
special antennas. One antenna is vertical and the other horizontal. Each antenna con-
sists of a multiplicity of collinear dipoles mounted along a wave-guide section and fed from
3 Mile
Precision scopes
10 Mile
Precision scopes
r—
-»
j*
"I
J
M
Magnetron
oscillator
T-R
box
»>
Het.
unit
•>*
Rec.
Synch,
unit
Spare
Spare
Spare
Spare
I Motor-dilvan 1 I
1 beam shift device |
FIG. 26. GCA Search and Precision Radar Equipment Arranged for One-man Operation
small probes projecting into the wave guide. The spacing of the dipoles and phase of
their currents create the sharp patterns required for precise direction determination.
These patterns are aimed along- the approach path and then made to oscillate rhythmically
across the path by shifting the dipole current phases (mechanically distorting the rear of
the wave guide through a motor-driven mechanism).
The received precision radar echoes are displayed on offset-center PPI scopes as illus-
trated in Fig. 26. This presentation and the narrow radiated beams permit the operator
to obtain great precision in the observation of aircraft displacement. The vertical antenna
gives the glide path displacement, and the horizontal antenna gives lateral displacement.
One unique feature in the GCA, which is used in certain other radar equipments, is the
optical system of the PPI scopes. The operator views an illuminated map through a 45°
glass plate. The scope is directed at the glass from a position complementary to the
position of 'the map below. The scope appears superimposed on the map. It is on the
map that the correct approach line is inscribed for use by the controller in detecting devia-
tion of the airplane. . . .
Three important features of GCA are: (1) No equipment is required in airplanes for
its use other than already existing communications. All aircraft then may use n. (2) Its
precision and straightness of path are unaffected by conditions surrounding the site, such
as buildings, hangars, and wires. (3) The precision is not entirely in the system but partly
in the ability of the operator to bisect the target image. (4) The identity of aircraft being
22-28 AIDS TO NAVIGATION
controlled depends largely upon the skill and attention of the operators. (5) Skill, practice,
and experience are required in any blind approach operation. In GCA this skill is on the
ground.
NAVA GLIDE (Federal). The navaglide instrument landing system being developed
by the Federal Telecommunications Laboratories is a microwave system using only one
frequency channel. The four-directional signals of the glide path and localizer indications
will operate on this frequency channel simultaneously through the use of a scheme of
subcarrier modulation. The receiver of the "Navar" navigation system (described below)
may be used, ultimately, also for the landing signals. Accurate distance-measuring
equipment will replace the markers of the present instrument landing system, permitting
use of automatic landing equipment.
MICROWAVE (Sperry). A complete microwave instrument landing system, operating
at approximately 2600 Me, has been developed and successfully operated experimentally
for several years by the Sperry Gyroscope Company. This development, now in pro-
duction status, overcomes objectionable siting and wave-reflection problems existing on
systems using lower frequencies. Reasonably small radiating systems are able to con-
centrate and confine the radiated energy to the approach sector and avoid nearby buildings,
wires, or hangars. Reflections from these objects on other instrument landing systems
causes course and path bends.
The present success of the system may be attributed to the development of the klystron
tube (2K36/416) for airborne receiver use and to the development of crystal control for
both the transmitting and receiving equipment.
The complete system consists of two ground stations (localizer and glide path) and one
airborne receiver. The ground stations are identical in electrical circuits and have equiva-
lent outputs of about 70 watts but use different radiating elements. The glide path
radiator is a tilted vertical parabola fed by two wave guides through a mechanical modu-
lator. The wave-guide feeds are displaced from the parabola focus in opposite directions
and therefore produce two overlapping patterns, the plane of overlap being inclined up-
ward at the desired approach glide angle. The patterns are amplitude modulated 600 and
900 cycles respectively. The parabola is narrow to give wide horizontal coverage. This
permits its being placed safely to the side of the runway.
The localizer transmitting antenna is a paraboloid, giving a relatively concentrated
pattern in both horizontal and vertical planes. It is equipped with a central vertical
dividing shield to separate the two wave-guide feeds. The radiated patterns overlap in a
vertical plane thereby forming a course for left-right guidance along the runway center
line. The localizer is placed on the runway center line at a safe distance from the end
opposite from that on which the airplane lands.
The one receiver used in the airplane has a common crystal-controlled klystron tube
oscillator serving two separate IF circuits. The filtered and rectified outputs of the two
channels are balanced and connected to the localizer and glide path pointers respectively
of the conventional crossed-pointer landing instrument. Two flag alarms on the instru-
ment serve as indicators to warn against failure of the localizer or glide path signals.
An electronic coupling device now in production is used to couple the localizer and glide
path signals into the Sperry (A-12) electric auto-pilot for automatic approach flight.
It works equally well on the CAA instrument landing system.
6. PROPOSED NEW SHORT-RANGE NAVIGATION SYSTEMS
LANAC (Hazeltine). The word "Lanac" is derived from * laminar navigation and anti-
collision."
This system is proposed for the 1000-Mc band and utilizes in each airplane an interroga-
tor and a replier. The replier consists of a pulse receiver and transmitter capable of auto-
matically replying to interrogating pulses of proper frequency and coding. The code
key of the replier varies with altitude layers in a prescribed standard manner, through the
use of an aneroid cell.
The interrogator includes a pulse transmitter, coded to challenge the repliers of other
aircraft, and a receiver to interpret the reply. Normally it interrogates on the code equiva-
lent to its own altitude so as to provide anticollision and traffic control safety. By means
of a switch, the interrogation code can be varied to scan the traffic in altitude layers above
or below the level being flown. The interrogator antenna is directional and rotatable so
that direction as well as distance and altitude of replies can be observed on the L-type (or
possibly PPI) scope used in the system.
Ground transponders and ground interrogator stations are included to permit route navi-
gation by the aircraft and ground surveillance of airways traffic overhead, obtaining posi-
PROPOSED NEW SHORT-RANGE NAVIGATION SYSTEMS 22-29
tion of planes in three dimensions as well as identity of each plane, and affording selective
signaling to each plane. The ground transponders also serve as obstruction warning units.
Ground transponders, properly placed on the approach, aid the airplane on instrument
approach to the airport.
The Lanac interrogator may be employed as a radar, in special applications, by tuning
the receiver and transmitter of the interrogator to the same frequency so that echoes will
be shown on the interrogator's display in the usual radar manner. In this case, of course,
no replier is utilized.
This radar mode of operation is used in an aircraft to supply terrain-clearance informa-
tion when the plane is flying at an altitude of 500 ft or more. It therefore offers an im-
portant safety feature for off-airway flying over mountainous country. The radar mode
is used in marine anticollision service to warn against unequipped craft. Radar anticol-
lision protection between aircraft is not feasible because of the small size of the targets and
their extremely high relative speeds when closing on a head-on-collision course.
The Lanac system is useful in marine navigation, and a description of this application is
given under Marine Aids.
TELERAN (RCA) (ieZevision radar air navigation) . Teleran is a comprehensive system
of navigation involving radar as the means of collecting air traffic information and tele-
vision as a means of displaying the information to the pilot. Radar stations with over-
lapping 50-mile service areas to form the airway are proposed. Respondors in every
airplane are essential, although failures of respondors can be taken care of in the plan by
using separate echo-type search radar equipment. The PPI picture obtained in the ground
radar is used by air traffic control or tower operators. This same picture, with any de-
sired obstruction, control, or weather instructions superimposed, is televised, transmitted
to, and repeated in the airplane by television.
The system permits both pilot and ground operator to see and appreciate the complete
air traffic situation. The airborne transponder units can be coded or varied automatically
with altitude to segregate the various flight levels and to permit identification of aircraft.
Instructions may be written out on the ground and "handed" to the pilot on the television
picture.
For landing at an airport, an airport localizer radar and GCA precision radar units are
proposed.
For each altitude level and for the echo-type search radar, separate television trans-
mitting equipment and radio-frequency channels are required. The channels required
can be greatly reduced over commercial television because a low scanning rate may
be used.
NAVAR (Federal) (navigational and traffic control radar). A system for traffic control
and navigation around airports and along airways. This system provides the following
features, which may be applied progressively to an airways system: (a) Ground radar
surveillance in the form of PPI displays, (b) Distance and azimuth information in the
airplane. The azimuth information is omnidirectional derived from the ground radar
system, (c) PPI traffic presentation in the airplane, relayed from the ground station.
(d) Selective signaling, ground to aircraft; and automatic identity and altitude response,
aircraft to ground.
The ground radar equipment and display is conventional except that provision is made
to separate known (respondor-equipped) aircraft from, others. The distance information
in the airplane is obtained by a pulse interrogating system. The azimuth information in
the airplane is obtained by measuring the time from the reception of a non-directional
pulse radiated from the ground to the reception of the rotating search radar beam. The
pulse and beam are synchronized for true north direction. The timing measurement in
the airplane is made automatically.
The airborne PPI display, called "Navascope," is obtained by sending synchronized
pulses omnidirectionally from the ground radar station. These pulses contain the in-
formation of all aircraft in the area as revealed on the ground radar scope and are repro-
duced in synchronism on the airborne PPI. The airborne PPI display includes positive
identification of observer's own airplane and self-centered altitude layer presentation.
Selective signaling of aircraft is obtained by directing a sharp "challenging" beam in
the direction of the airplane on which a check-up is desired. The aircraft respondor
beacon circuit is to contain a double-pulse gate. The gate is tied in with the aircraft
distance indicator, so that it varies with distance. The interrogating pulses, beamed from
the ground, are spaced automatically as the operator selects the distance range of the
target he wishes to challenge. Thus the challenge is narrowed down to distance and
direction.
The complete system proposes one airborne transmitter and two receivers. This does
not include communications equipment.
22-30 AIDS TO NAVIGATION
MICROWAVE OMNIDIRECTIONAL RADIO RANGE (Sperry). A radio range
operating on the same general principles as described for the CAA VHF omnidirectional
range, but in the microwave frequencies (2600 Me), has been developed by the Sperry
Gyroscope Company. Like the CAA system, it utilizes the comparison of phase between
two audio waves in the airplane to determine the azimuth bearing to the station. In
the microwave system, however, the antenna of the ground station is so small that it
can be rotated at 1800 rpm, thereby avoiding the use of a capacity goniometer and avoid-
ing antenna phasing problems.
In this system, as in the Sperry microwave instrument landing system, the cw signal
to be radiated is generated by a crystal-controlled klystron tube. A synchronous 1800-rpm
motor drives a small alternator, the output of which frequency-modulates a 70-kc sub-
carrier. The subcarrier, as in the CAA system, amplitude-modulates the microwave
carrier. The modulated carrier is conducted to an antenna system consisting of a vertical
stack of three small loop antennas. The stack gives vertical directivity for maximum
horizontal coverage. The modulated carrier radiation produces the reference audio
voltage in the airborne receiver. Its relative phase is the same in all azimuthal directions.
The vertical stack of antennas also has a directive pattern in the horizontal plane. This
horizontal pattern is essentially sinusoidal. By rotating the pattern, with the same motor
as used above, another audio voltage is generated in the receiver. This voltave wave,
with respect to the former reference voltage wave, has a phase that varies with position
around the station. For the full 360° around the station there is a complete cycle or 360°
phase variation in the wave. This is called the variable signal. By comparing the phase
between this variable and the former reference signal the bearing from the station can be
determined.
The phases may be compared in the same manner as in the case of the CAA range, or
the phase detector may be used to control the operation of a motor which turns a map in
accordance with movement of the airplane around the station.
The proposal for the complete system includes the addition of distance-measuring signals
and communications through the single ground station transmitter and antenna.
The greatest advantage in the use of the proposed system is the elimination of the
goniometer through the rotation of the antenna system. Reduction in the amplitude of
course bends due to siting (reflections from buildings, trees, etc.) are evident.
AEROTRONICS (Raytheon). The Aerotronics system is a proposal based on radar
technique and uses PPI scope presentation in the airplane and on the ground. It includes
(1) airborne radar, (2) ground beacons (transponders), (3) ground radar, (4) airborne
transponders, and (5) distance-measuring equipment. With this equipment, navigation,
collision prevention, airways traffic control, approach, and landing are to be taken care of
without other aids.
The airborne equipment includes a rotating antenna for radar search, an omnidirec-
tional antenna for communications, and an antenna for distance measuring. The ground
radar includes both azimuth and elevation search. This is for traffic surveillance and
control. Ground beacons (transponders) would be used for route navigation.
The distance-measuring equipment proposed operates on the principle of the optical
interferometer. It operates a counter at the ground traffic control station where distance
to the airplane may be observed with great accuracy.
MULTIPLE TRACK RADAR RANGE (Australian). A multiple track radar range
(MTR) has been developed and successfully demonstrated by the Council for Scientific
and Industrial Research of Australia at Sydney. This range produces visually indicated
(left-right) , positively identified flight tracks, based on the time of arrival of pulses from
two spaced ground stations. VHF (212 Me) is employed, which results in line-of-sight
distance coverage. The tracks are hyperbolic in shape, but essentially straight beyond
20 miles. The tracks or courses are fly able to within about ±1°.
The MTR system is fundamentally the same as GEE, a British development used
extensively in the invasion of Europe, except for type of presentation. GEE is a hyperbolic
system similar to Lor an. except for its frequency. Two stations only are used in the MTR
system, one a master, sending a series of equally spaced pulses (5000 pps in this case) of
peak power about 10 kw. The second, a slave station, is equal to the master, but spaced
about 8 miles distant and normally inoperative. The slave station receives the pulses
from the master and rebroadcasts them with a suitable fixed time delay. For any position
around the pair of stations, the pulses are received in a specific time relationship. The
contours of equal time differences are hyperbolas passing between the stations and are
used as tracks or courses. Non-directional, vertically polarized antennas are used.
In the airborne equipment, the pulse signals are compared in an automatic circuit
similar basically to that in the distance-measuring equipment described before. Standard
time differences chosen as the tracks are set up on a calibrated switch dial and numbered
MISCELLANEOUS RADIO AIDS 22-31
(track numbers 1 to 30) . When a given track is selected, a left-right indicator signals the
pilot any deviation from that track.
The master and slave stations are separated in the receiver by permitting the master
(only) to transmit double pulses. MTR equipments at adjacent places are identified by a
selected difference in repetition rate.
Distance-measuring equipment, of the interrogator-respondor type, is proposed for use
with the MTR system.
7. PROPOSED NEW LONG-RANGE NAVIGATION SYSTEMS
CAA LOW-FREQUENCY OMNIDIRECTIONAL RANGE. The low-frequency omni-
directional range operates like the VHF omnidirectional range, i.e., in the comparison of
the phase of two audio signals. In early tests of this range, two individual, basic, carrier
frequencies were used — one at 172 and one at 194 kc.
The low-frequency omnirange consists of the conventional five-tower Adcock antenna
array, one tower at each corner of a square and the fifth tower in the center. The ref-
erence signal, 172-kc carrier, modulated with 30 cps, is fed into the center tower only and
is, therefore, radiated non-directionally. The other signal (194 kc) is fed to the corner
towers through an inductive goniometer which is mechanically rotated at 1800 rpm. The
rotation of the goniometer spins the figure-of-eight pattern of the corner towers, producing
the variable phase signal in the aircraft receiver. When compared to the phase of the
reference signal in a wattmeter circuit, it can be made to indicate azimuth.
Tests are being conducted using a single low frequency and a subcarrier of 1000 cps.
The 30-cps reference is applied to this subcarrier by frequency modulation, as in the case
of the VHF.
The wattmeter indicating circuits are the same as those used with the CAA VHF omni-
receiver,
Night effect represents a serious problem for radio ranges. The lower the frequency
employed, the greater is the ground wave signal strength and the more stable will be the
operation of the system. Night effect is minimized by curtailing the amount of unwanted
vertical radiation. The fact that the signal arrives via ground or sky does not, in itself,
introduce an error in the omni system since the indication does not depend upon the length
of the path. The development may result in much more freedom from night-effect errors
and swinging than in an automatic direction finding system employing a loop and operating
on the same frequency.
SONNE (Consul). This is a German aural CW system used against the Allies during
the war and capable of great accuracy over long distances and useful in both air and
marine service. For its description, refer to Marine Aids, article 10.
LORAN (Z0ng-range air navigation). Excellent results are being obtained in the ex-
tensive use of Loran in transoceanic flights. For a description of this system, refer to
Marine Aids, article 10.
NAVAGLOBE (Federal). This is a CW system using very low frequencies for long-
range navigation over oceans and continents. The receiver proposed has a narrow-band,
noise-rejecting feature and ADF facilities. The ground station consists of three antennas
spaced in the corners of an equilateral triangle, and a transmitter which is connected in
succession to the three antenna pairs each second. Three dumbbell-shaped patterns,
displaced in bearing by 120° from each other, are radiated successively. Relative ampli-
tudes of the three successive signals received during each cycle are measured automatically
by a ratiometer, permitting direct visual indication of bearing at all azimuths from the
station. For other directions between courses, measurement of ratio in a ratiometer in
the receiver permits determination of relative "bearing with respect to the antenna array.
8. MISCELLANEOUS RADIO AIDS
VERTICAL SEPARATION INDICATOR. The Stratoscope is an instrument con-
ceived to provide visual indication in an airplane and on a ground monitor of the vertical
separation between airplanes (or other obstacles) within a minimum service area of 10
miles distance and 1000 ft elevation.
Basically, the Stratoscope operates by converting aircraft height into frequency and
then utilizing panoramic reception to display received signals along a CRT time base
calibrated in relative vertical height. The airplane equipment includes a transmitter
and a receiver-indicator unit. The ground monitor needs only a receiver-indicator
unit.
22-32 AIDS TO NAVIGATION
Conversion of height into frequency is accomplished by means of a precision aneroid
cell which operates a variable tuning condenser in a coaxial line oscillator. The oscillator
frequency changes 5 Me in 10,000 ft. This change is accomplished in the frequency band
of 148-154 Me. The height of the transmitter in relative pressure altitude may therefore
be determined by measurement of transmitter frequency.
Interference from the plane's own transmitter is avoided by sharing time between the
transmitter and receiver at an alternation rate of 30 cps. By coding the transmission,
some identity of the airplane can be provided in the receiving indicators.
In tests of this equipment an accuracy of 200 ft was observed. The required 10- or 20-
mile distance range can be covered with about 5 watts (transmitter power output).
ABSOLUTE ALTIMETERS. Absolute altimeters have little utility in navigation over
land because of the rapid variation in indication in rough territory, but they do have
utility in navigation over water, which is flat, as a means of maintaining constant height
above the surface. Variations then in the pressure altimeter indicate flight toward or
away from atmospheric-pressure areas. Flights directed laterally so as to give constant-
pressure altimeter reading (for constant absolute altitude) avoid storm areas over the
oceans.
Many absolute altimeters have been invented over a period of twenty years, including
sonic, capacity, frequency modulation, and radio-pulse types, A reference is given for
detailed information as space permits only summary remarks here.
One absolute altimeter, called a "terrain clearance indicator," was developed for com-
mercial use just before the war. It operates on the FM principle at about 432 Me. The
transmitter continuously radiates its energy downward from a doublet antenna. The
frequency is varied from 410 to 445 Me sixty times per second. The receiver takes in the
energy reflected back from the ground and also some of the original transmitted energy.
The receiver output, which may be considered a beat between the two signals, has a
frequency depending upon and increasing with altitude.
The FM type absolute altimeter is capable of operating down essentially to zero altitude.
It has greatest accuracy at lowest altitude but is subject to possible serious errors from
adjustment and noise which prevent its immediate use on instrument landing.
The radiopulse altimeter developed during the war for high-altitude bombing uses a
cathode-ray tube as a means of displaying time between transmitted pulse and echo. The
display is calibrated in feet of altitude and arranged circularly around the tube face.
Essentially it is a radar distance indicator with its antenna fixed in a position under the
airplane. The pulse type altimeter is extremely accurate at high altitude but, at present,
useless at altitudes below several hundred feet. Future development may bring about
reduction in this minimum altitude.
REFERENCES
GOVERNMENT— CAA
The U. S. Dept. of Commerce — How It Serves You on Land and Sea and in the Air. U. S. Government
Printing Office (January 1946).
The FCC Allocation Plan, Electronics, March 1945, p. 92.
Advancing Air Navigation. U. S. Government Printing Office (1946).
FOREIGN
xline Navigation Was Different in
0 , Aircraft Radio Eauit>ment for Us
p. 979.
Gravis, Airline Navigation Was Different in Europe, Aviation Mag., November 1940, p. 40.
Hodgson, Aircraft Radio Equipment for Use on European Air Lines, Proc. I.R.E., September 1935,
RADIO RANGES— LF
Diamond, On the Solution of Night Effects and the Radio Range Beacon System, Proc. I.R.E., June
1933, p. 808.
Jackson-Stuart, Simultaneous Radio Range and Telephone Transmission, Proc. I.R.E., March 1937,
p. 314.
Army-Navy Precipitation Static Project, Parts I to VI, Proc. I.R.E., April 1946, p. 156P; May 1946,
p. 234P.
RADIO RANGES— VHF
An Ultra-high-frequency Radio Range with Sector Identification and Simultaneous Voice, Electrical
Comm., June 1946, and Proc. I.R.E., January 1946, p. 9W.
Development of the VHF Radio Range, Part III, U. S. Dept. of Comm. CAA T. D. Report 49.
RADIO MARKERS
Jackson, Metz* McKeel, Test of First Manufactured Fan Marker, U. S. Dept. of Comm. CAA T. D.
Report 15 (July 1938).
Hromada, Development of New Station Location or 1 Marker, Proc. I.R.E., August 1944, p. 63. '
LaPort, Radiating System for 75 Me Cone of Silence Marker, Proc. I.R.E., January 1942, p. 26.,
RADIO AIDS TO MARINE NAVIGATION 22-33
AUTOMATIC DIRECTION FINDERS
Roberts, H. W., Aircraft Direction Finders, Chapter 8, p. 190. Morrow, New York.
COMMUNICATIONS
Ellihorn, Anti-noise Characteristics of Differential Mies, Proc. I.R.E., February 1946, p. 84P.
Shawn, Application of the Throat Mic, Communications, January 1943, p. 11.
Bennett et al.f The Design of Broad Band Aircraft Antenna Systems, Proc. I.E.E., October 1945, p. 671.
AIR TRAFFIC CONTROL AND WEATHER
Air Traffic Rules, CAA Manual 60. U. S. Government Printing Office (October 1945).
Gilbert, Future Air Traffic _ Control, Flying Mag., April 1946, p. 60.
Diamond, Recent Applications of Radio to Remote Indication of Meteorological Elements Elec. Eng.,
April 1941, p. 163.
Hauck, Radiosonde Telemetering Systems, Electronics, May 1946, p. 120.
Is the Air Full, Harper's (July 1946).
INSTRUMENT LANDING
Instrument Landing of Aircraft, Elec. Eng., December 1940, p. 495.
Metz, The CAA-RTCA Instrument Landing System, U. S. Dept of Comm. CAA T. D. Reports 35
and 36 (October 1943).
Caporale, The CAA Instrument Landing System, Electronics, February 1945, p. 116; March 1945,
p. 128.
Metz, Radio Glide Path for Aircraft, Radio News, November 1945, p. 8.
Montgomery, A VHF Aircraft Antenna for Reception of 109-Mc Localizer Signals, Proc. I.R.E.,
November 1945, p. 767.
OMNIDIRECTIONAL RADIO RANGE
Luck, Omnidirectional Radio-Range System, R.C.A. Rev., March 1946, p. 94,
Stuart, The Omni-Directional Range, Aero Digest (June 15, 1945).
RADAR
The Radar Equation, Electronics, April 1945, p. 92.
Schneider, Radar, Proc. I.R.E., August 1946, p. 528.
NEW LANDING SYSTEMS
Ground Controlled Approach for Commercial Aviation, Electronics, May 1946, p. 160.
Spicer, The GCA Landing Systems, Bendix Radio Engineer, January 1946, p. 17.
Folland, The Use of Microwave for Instrument Landing, Radior April 1946, p. 23.
Aerial Navigation and Traffic Control with Navaglide, etc., Electrical Communication, June 1946, p. 113.
ROUTE NAVIGATION
Herbst et al., The Teleran Proposal, Electronics, February 1946, p. 124.
Aerial Navigation and Traffic Control with Navar and Navaglobe, Electrical Communication, June
1946, p. 113.
Pierce, Introduction to Loran, Proc. I.R.E., May 1946, p. 216.
Sandretto, Absolute Altimeters, Proc. I.R.E., May 1944, p. 167.
Frequency, Power and Modulation for Long-range Radio Navigation System, Electrical Communica-
tion, June 1946, p. 144.
RADIO AIDS TO MARINE NAVIGATION
By M. K. Goldstein
Table 1 shows an extensive summary and classification of established, recently intro-
duced, contemplated, and proposed electronic aids to marine navigation. It will be
noticed that the systems are classified in groups dealing with radio types, sonic and super-
sonic types, and red and infrared types. Also the various systems are analyzed for essen-
tial characteristics falling into the following grouped categories: Type of system (including
basic principle and position information supplied) ; performance of system (including range,
accuracy, ambiguities, operating frequency, and band width; system requirements (in-
cluding required ship and shore equipments) ; and the system usability (including engineer-
ing status and reliability factors) . Details concerning each of the specific systems classified
are discussed in the following articles in this section.
22-34
AIDS TO NAVIGATION
Table 1. Summary and Classification of Established, Recently
System
Type
Performance
Principle
Employed
Basic
Information
Supplied
Maximum *
Range
Accuracy 2
Ambigu-
ities
Frequency
(Mc/s)
RADIO
a. Radiobeacon
"Azimuth
Short, med.
<2°
None
0.285-0.3153
(shore)
b, Radiobeacon
(ocean sta.) t
c. Radar marker
(Rarnark)
d. Respondor
Non-directional
transmission and
directional
reception
Azimuth
• Azimuth
R & az. fix
Medium
Optical
Optical
Devel'pm't'l
±2%, ±3°
None
None
None
0.30-0.55
3, 5, & 10 cm.
3, 5, & 10 cm.
(Racon)
e. Reflector (Racon) .,
f. Rotating beacon
Dir. trans. & non-
R & az. fix
Azimuth
Optical
Medium
±2%, ±2°
None
Multiple *
3, 5, & 10 cm.
0.20-0.5
(Consol.)
dir. reception
2. Direction finding— ship
(Loop):
a. MF— Aural null "
"Azimuth "
X2°
None
0.3-3.0
(Standard) t
b. MF-Nuli seeking
Azimuth
<2°
None
0.2-1.75
(ADF)
(SCR-269) f
c. MF-Instantaneous
(DAK) f
d. MF— Position plot
Directional
reception of any
transmission
Azimuth
Az.fix
Normal
communi-
cation
range
'<2°
None
None
0.25-1,5
0.1-1.6
(Bendix)
e. HF— Instantane-
Azimuth
5°-10°
None
1.5-21
ous (DAQ,
, DAU)f
.
3. Direction finding— shore: t
a. MF-Adcock i
r Azimuth 1
M°-2°
None
0.25-1.5
(DAH)
Normal
I
b. HF-Adcock
Azimuth !
communi-
None
1.5-30
(DAJ.SCR-291)
c. HF — spaced loop
(DAB)
d. VHF-Adcock
Directional
reception of any
transmission
Azimuth J
Azimuth
cation
range
Optical
3°-4°
3°-5°
None
None
2.0-18
100-160
(DBF)
e. UHF— Reflector
Azimuth
Optical
3°-5°
None
90-5000
(DBM) J
.
4. Radar:
a. Ship
Echo ranging
R & az. fix
Optical
±2%, ±2°
None
3, 5, & 10 cm.
b. Shore
Echo ranging
Traffic
Optical
±2%, ±2°
None
3, 5, & 10 cm.
5. Propagationtimedifference
a. Loran (stanoard) . "
•HypLofP 7
Long
0.5%
None8
1.7-2.0
b. Loran (SS) 10
PTD 6— synch.
HypLofP
Long
0.5%-1.0%
None?' is
1.7-2.0
c. Loran (LF)11....
pulsed trans-
missions
' HypLofP
Long
<i.o%
NoneS
0.18
d. Gee
Hyp fix
Optical
<0.8%
None 8
20-85
e. Decca j
PPD "-Synch.
[Hyp fix
Medium
±0.02% i*
Multiple"
O.Ot-0.2
f. POPI f
CW transmis-
sions
HypLofP
Long
Devel'pm't'l
None
0.75
6. Interrogator-respondor:
a. Shoran . . .
Dual beacon
Range fix
Optical
±50 ft
Few16
210-320
b. Lanac— ship
ranging
Single beacon
R&az.fix
Optical
±2%, ±2°
None
1000
ranging
c. Lanac — shore
Single beacon
Traffic
Optical
±2%, ±2°
None
1000
ranging
7. Composite data relay:
a Teleran
Instant, data relay
Gen. nav.
Optical
Telv. Ch'n'l
b. Facsimile
Recording data
Gen. nav.
Medium
Facs'm'le
relay
Ch'n'l
RADIO AIDS TO MARINE NAVIGATION
22-35
Introduced, Contemplated, and Proposed Aids to Marine Navigation
Performance
Requirements
Appraisal Factors *
Signal
Band Width
Minimum Equipment for Basic
Information Supplied
Engineering
Status
General Remarks
Ship
Shore
>CW
DF receiver
Coded beacon
Proven
Inaccurate and unreliable beyond predom-
£CW
DF receiver
Coded beacon
Proven
inant ground wave range.
Combination radiobeacon, rescue ship,
weather station.
3-5 Me
Special radar
Beacon
Under develop-
Identified by reference to natural target
ment
3-5 Me
Special radar
Respondor beacon
Proven
Identification obtained by coded transmis-
3-5 Me
<lkc
Radar system
Receiver
Reflector
1 station
Proven
Under trials 6
sion.
Special target for increased echo reflection.
Minimum range — 25 mi; accuracy deteri-
orates at night beyond predominant
ground wave range.
£CW
Standard DF "|
"Proven
£CW
Special DF
Proven
2a to 2e inclusive— unreliable beyond pre-
:>CW
Special DF
2 ADF'S & computer
CW or other
transmitter
Proven
Under de-
velopment
dominant ground wave range due to sus-
ceptibility to polarization error.
Note to 2d: Fix obtained by simultaneous
cross-bearing plot on map.
£CW
Special DF
Proven
I
£CW
MF transmitter
Special DF
Proven
£CW
HF transmitter
Special DF
Proven
3a to 3e inclusive — designated models have
:>CW
HF transmitter
Special DF
Proven
low susceptibility to polarization errors
beyond ground wave ranges. Indicated
>cw
VHP transmitter
Special DF
Proven
accuracies generally realized up to maxi-
mum sky wave range.
;>cw
UHF transmitter
Special DF
Proven
3-5 Mo
Radar system
None
Proven
Valuable anti-collision and short-range
*
naval device.
3-5 Ms
Comm. receiver
Radar, comm.
Under trials
Suitable for traffic control in congested areas.
transmitter
50-70 kc9 -
"2 stations
Proven
Day range, 750 mi; night range, 1400 mi
(over sea water).
50-70 kc 9
Special receiver and indi-
2 stations
Under trials
Night use only; utilizes base line of approx.
100 mi.
10 kc
cator
2 stations
Under trials
Greater ground wave range and more stable
1 Me 12
- 3 stations
Proven 5
propagation over 5a.
Simultaneous fix from 2 hyperbolic lines ot
position.
3CWfreq's.
Special receiver
3 stations
Under trials 20
Limited as 1 (a) above owing to ionospheric
phase shifts.
<1kc
Rcvr. & Spc'l ind.
1 station
Under develop-
ment5
Same as 5e; awaits satisfactory phase meas-
urement between sequentially received
signals.
3-5 Me v }
f 2 respondor
Proven u
Bombing and mapping aid; may have marine
1
3-5 Me [
Special trans. & receiver
J beacons
| Respondor
Under trials
use.
Optional operation: radar beacon or radar
J
[ beacon
system.
3-5 Me
Respondor beacon,
Spc'l. trans. &
Under trials
Traffic control utilizing shipboard trans-
comm. receiver
rcvr., comm.
ponders.
trans.
3-5 Me
Television receiver
Television
Under develop-
Air traffic control system; also feasible for
transmitter
ment
marine use.
1-1 Okc
Facsimile recejver
Facsimile
Proven
Permanent recording of any general infor-
transmitter
mation, data, etc.
22-36
AIDS TO NAVIGATION
Table 1. Summary and Classification of Established, Recently Introduced,
System
Type
Performance
Principle
Employed
Basic
Information
Supplied
Maximum 1
Range
Accuracy 2
Ambigu-
ities
Frequency
(Kc/s)
SONIC AND
SUPERSONIC
8. Underwater beacon
Non-dir. trans. &
dir. reception
Dir. reception of
any transmission
Gen. echo ranging
Vert, echo ranging
PTD 6— Explosion
& multiple timed
reception
Non-dir. trans. &
dir. reception
Dir. reception of
any transmission
Optical echo
ranging
Azimuth
Azimuth
R & az. fix
Depth
Position fix
Azimuth
R & az fix
V short
V short
V short
V short
Vlong
V short
V short
U short
<r
±1°
<1%, <1°
<1%
<5mi
<1°
<r
Proposed
None
None
None
None
None
None
None
None
0.8-30
0.8-30
15-30
0.8-30
0.05-1.0
9. Direction finding
10. Sonar:
a. General echo ranging
b. Echo sounding
1 1 Sofar t
RED AND
INFRARED
1 2 Beacon
Microns 19
Far Infrared
(0.7-13)
Far Infrared
(0.7-13)
Near Infrared
(0.3-1.5)
1 3. Direction finding
14. Rcdar ...
* Based on data available up to late 1949.
t Used entirely or in part for distress service.
1 Ultra-short 0-1 nautical miles
Very short 1-10 nautical miles
Short 10-150 nautical miles
Medium 150-500 nautical miles
Long 500-1500 nautical miles
Very long over 1500 nautical miles
2 Representative accuracies obtained in practice.
3 Frequencies in' current U. S. use.
4 Resolved by dead reckoning or DF.
6 British only.
6 Propagation time difference.
7 Hyperbolic line of position.
8 Two easily resolved ambiguities can exist in fix obtained.
9 Provisions are made for 16 different channels on the same
carrier frequency by utilizing different pulse repetition rates.
9. ESTABLISHED NAVIGATIONAL AIDS
RADIOBEACON SYSTEMS (MF) (See references 2 and 3.) The non-directional
medium-frequency (MF) radiobeacon system, maintained by the Coast Guard in the
United States and by similar organizations in foreign countries throughout the world, is
the most extensively used radio navigational aid today. The system consists of fixed
radiobeacon stations located at lighthouses, lightships, and other points, which transmit
distinctive identifying coded tone signals, enabling navigators at sea to take bearings on
them by means of medium-frequency loop direction finders. Bearings obtained from two
or more such beacon stations, in conjunction with charts of the geographical locations of
the radiobeacons, uniquely establish the ship's position. A single radio direction-finding
(DF) bearing crossed with a line of position of a heavenly body, two bearings on the same
station and the distance run between bearings, or a bearing and a synchronized air or
submarine fog signal also suffice to determine the position of the vessel. In the last case,
blasts from the sound signal are synchronized with the radiobeacon signals and the differ-
ence in time of reception of these two signals can be converted into an approximate station
distance. Owing to the many factors which enter into the transmission and reception of
radio signals, a ship cannot estimate its distance accurately from a radiobeacon either by
the strength of the signal received or by the time at which the signals were first heard.
However, a line of direction obtained from a single radio bearing enables a ship to proceed
toward the radio station by the shortest course. This is especially applicable to a rescue
ship, enabling it to head directly toward the ship in distress and thereby arrive in the
minimum of time. Such radio bearings are usually accurate to within 2° or less, depending
upon the equipment and the operator's skill. DF calibration transmissions are available
from radiobeacons upon request, continuous signals being transmitted while the ship's
direction finder is being calibrated. The simplicity and reliability .of the radiobeacon
indicate that such systems will continue to exist as a navigational aid for many years.
The present MF radiobeacon system in the United States (see Fig. 1 for East Coast
and Gulf) consists of approximately 200 radiobeacons, each radiobeacon operating on
one of the even frequencies in the 285-315 kc/s band. The European system frequency
ESTABLISHED NAVIGATIONAL AIDS
22-37
Contemplated, and Proposed Aids to Marine Navigation — Continued
Performance
Requirements
Appraisal Factors *
Signal
Band Width
Minimum Equipment for Basic
Information Supplied
Engineering
Status
General Remarks
Ship
Shore
£CW
£CW
1-4 kc I
1-4 kc
< 1000 eye
Sonic DF
Sonic DF
Special transmitter and
receiver
Special explosive charge
Infrared DF
Infrared DF
Special transmission and
receiver
Sonic beacon
Any sonic
transmission
fNone
JNone
Special receiver
stations
Infrared beacon
Any infrared
transmission
None
Proven
Proven
Proven
Proven
Tinder trials
Proven
Proven
Proposed
Usefulness limited by certain underwater
phenomena; see 10 (a).
Bearing on any received underwater sound
transmission; see 8.
Accuracy subject to underwater refraction
and propagation.
Depth finding by reflected sound transmis-
sions.
Proposed distress aid using natural under-
water sound channel.
Same range as visual light under fog condi-
tions.
Same range as visual light under fog condi-
tions.
Same range as visual light under fog condi-
tions.
Microns
Apr>rox. 13
Approx. 13
3.2
10 Intended to increase nighttime accuracy over Standard
Loran; however, comparable accuracy has not yet been prac-
tically achieved.
11 Intended for increased daytime range over Standard
Loran; however, comparable accuracy has not yet been fully
realized.
12 If necessary, different pulse repetition rates will permit
multistation operation on same carrier frequency,
13 Propagation phase difference.
14 For medium range.
15 Resolution awaits satisfactory system of "lane" identi-
fication.
16 Solved by general knowledge of position.
17 Air only.
18 Four-station operation also provided to give increased
accuracy and to remove ambiguities.
19 The thousandth part of 1 mm.
20 A British Isle Deeca facility is in 24-hr operation with
performance results indicating a proven system.
band is 290-320 kc/s. Distinctive signals, by which the different stations are positively
identified, are obtained by keying a tone-modulated carrier to give simple dot-dash com-
binations at the rate of thirty characters per minute. Because of the great number of
stations and the restricted frequency band, it has been found necessary to share time
between stations on the same radio frequency by transmitting signals from any one radio-
beacon for 1 minute followed by 2 minutes of silence. This allows two adjacent stations
to transmit similar signals on the same frequency without causing interference simply
by timing the transmissions to occur during successive minutes. Two-tone modulation is
used on some stations in congested traffic areas to add distinctiveness to the identifying
signal. During clear weather the radiobeacons follow such cycles of transmission for one
or two 10-minute periods of the hour. All six 10-minute periods are utilized during condi-
tions of fog. The beacons are carefully timed and remotely monitored.
Radiobeacons are grouped into four classifications, according to their power, output and
maximum effective ranges:
Class A 750 watts— 200 miles
Class B 150 watts— 100 miles
Class C 25 watts— 20 miles
Class D 5 watts — 10 miles
A few special high-power beacons having ranges of 400 miles have also been put into opera-
tion. Class A and B stations require identical equipment with the exception of the 750-
watt power amplifier used with the A stations. The transmitter, which is coupled directly
to the antenna for the B station, is used as an exciter for the power amplifier of the A sta-
tion. Both types of radiobeacons often use 125-ft insulated self-supporting towers as
non-directional antennas, with provision for location up to several hundred feet from the
transmitter house when local conditions make such an installation preferable. Sometimes
an insulated guyed antenna, approximately 40 ft high, is placed on top of a light tower
above the lantern. Lightships use vertical or symmetrical T antennas. Inverted L-type
antennas are not used because of the undesired directivity and the horizontally polarized
field components. The frequency of the A and B stations can be quickly changed to any
22-38
AIDS TO NAVIGATION
one of four pre-set frequencies which are usually crystal-controlled. Class C radiobeacons
are used for short-range navigation. The equipment is very similar to that of a class A
station except for the much lower power and the reduction in size of equipment. Owing
For CANADIAN RADIOBFACONS
7°" «e CANADIAN LISTS. «1
<> i
MANANA ID. 300 [Ml
HALFWAY ROCK 312 [3-D 01 SEAL 10 (CAN I 301 [2-5]
RACHOBEAC0N SYSTEM wate
COAST
' SOSTON Q1ST
vv> Off HJP i fitf&TQWHCWSIfipttlSN
- NEV\r>YQ&K DISt
MAKTUCKETL! 3M fJ-J) (WARNING BEACON)
T , /^ A
"j I A. I F1YWB PAN LS, 2S* [j.JJ
UNITED STATES and CANADIAN radlqbeacons are assigned group I
quencies and definite operating minutes. The sequence within a group
indicated by a Roman numeral before the name, thus IT. Stations with t
same sequence numerals transmit on the same minute.
diobeacons operate during fog or low visibility and during one or two
10 minute periods out of each hour in clear weather, (except stations at
CANAL APPROACHES which operate on scheduled periods only and
Cape Henry which operates continuously In assigned sequence, 1 minute on,
2 minutes off. 24 hours daily.
The scheduled 10 minute periods of each hour of clear weather operation
are given in brackets aftar the name of the sution, thus [1-4] [2-5] etc
(See clock face diagram). The last minute of each clear weather 10 minute
period Is silent
Washington. D.C.,Mar. 1, 1946
FIG. 1. Typical Radiobeacon. Navigational Chart, Published by U. S. Coast Guard
to the necessity of making the signals from these short-range stations especially distinctive
in areas of considerable marine traffic, the modulating audio frequency is variable in four
steps. The timer cams can be set to give a single tone or any combination of tones. Class
D marker radiobeacons are small automatic battery-operated transmitters located on
pierheads, buoys, ends of jetties, etc., which serve as local markers to indicate channel
entrances, turning points, etc., where careful approach is required. They are not syn-
ESTABLISHED NAVIGATIONAL AIDS 22-39
chronized with other radiobeacons but operate continuously in all types of weather,
sending out a characteristic of several dashes during each 30-sec period. The transmitter
frequency is crystal-controlled and has a modulation frequency of 1000 cycles per second.
A 15-ft welded Monel tripod mast is normally used as the antenna. Special warning
transmitters are located at some radiobeacons; each transmitter operates on the same
frequency as the beacon and gives a distinctive signal to warn a navigator who is homing
into the station that he is approaching dangerously close. The usable range of these
warning beacons is, therefore, intentionally reduced to provide warning over only a small
but sufficient area surrounding the long-range beacon.
At present the characteristics of some of these stations are being changed to provide
satisfactory operation with automatic direction finders. Instead of both the carrier and
modulation being interrupted during the keying process, only the modulation will be
interrupted. In addition, many of the stations will transmit throughout the hour under
all weather conditions rather than just during one or two 10-niinute periods.
The well-established aerobeacon system used for air navigation is also used for marine
purposes and is discussed in the first part of this section.
DIRECTION-FINDING SYSTEMS. (See references 4, 5, and 6.) The use of shipboard
medium-frequency radio direction finding has continued to grow as a navigation aid since
the early days of radio broadcasting. By use of the shipboard direction finder, practically
every transmitting station within the frequency band and range of the radio direction
finder is a potential point for a navigational reference line of position. Shipboard direction
finding also plays an important role in directly guiding vessels to other vessels in distress.
As an additional aid to navigation in time of distress, medium-frequency direction-finding
stations Ipcated along the coasts and on the Great Lakes are available to mariners who
transmit signals on the international distress frequency of 500 kc/s. Various other fre-
quencies are available for distress and emergency purposes, depending on the range from
land or the location of the vessel. For example, 8280 kc/s is used for United States long-
range contact and 2182 kc/s is used on the Great Lakes.
While the most widely used shipboard direction finder is of the loop aural-null type,
other types are available (see Section 6, article 32).
Environmental Effects. (See reference 5.) The term "environmental effects" is used to
describe all local physical conditions which cause DF bearing errors aboard ship and at
shore stations. Such conditions normally involve metallic structures near the DF antenna
and their radiation fields, induction fields, or shielding effects. For frequencies below 1000
kc/s, shipboard environmental effects can be sufficiently well controlled or compensated
(further details are given by C. T. Solt, Proc. I.R.E., Vol. 20, p. 228, February 1932) so
that direction finders in this band give highly satisfactory performance on ground-wave
transmissions; i.e., the resultant calibration curve is fairly symmetrical and does not
exceed a few degrees maximum deviation. Arriving signals of certain frequencies cause
partial or complete resonances in, and consequent reradiation and induction fields from,
nearby metallic structures. These fields generally impart 90° phase components (called
quadrature effects) to the arriving wave fronts, altering their apparent arrival direction
by amounts depending on the positions and sizes of the resonating structures. These
changes in direction result in deviations of the observed bearing from the true bearing.
Deviation, then, is defined as the quantity that "must be added algebraically to the
observed bearing in order to make it equal the correct bearing"; the deviation, however,
does not affect the resolving power (angular sensitivity) of the DF. The quadrature
effect, on the other hand, causes an elliptical polarization condition of the E or H fields,
or both, which generally results in failure of the antenna to find a sharp null coupling posi-
tion to these fields, thus adversely affecting the resolution of the DF. Figure 2 (a) shows
the maximum deviation that may be expected due to induced currents at frequencies at
which the structure may be resonant (worst case). For frequencies off resonance and
/<0.5 the shapes of the curves of Fig. 2 (a) are maintained, but the magnitude of the devia-
tion is reduced approximately as follows:
D
D = ^*: * (2)
1 + /<?[! - (/o//)T
where e is the voltage induced in the structure at frequency, /; r, x, L, C, and Q are the
electrical constants of the structures; Z>res. is the maximum deviation at the resonant
frequency /0; and D is the maximum deviation at any frequency. The resonant frequency,
/o, of structures may be determined from Fig. 2(6), to which some corrections should be
22-40
AIDS TO NAVIGATION
._ Hr_ Reradiated field . n ^Q
Hd Direct field ' r
D^stan*1 (F;)= greatest possible deviation
H=overall height of a % wave (grounded 0, H) or % wave (dlpoFe H,-H) reradlafor
1
F~
F=.0125 F=.015
D=.70° JD4.85
10H ' '
Note:
Solid curves use 0-9H abscissa
Dotted curves use 0-90H absc ssa
-H
10H
20H
60H
70H
30H 40H 50H
Spacing from reradiator
FIG. 2 (a). Bearing Deviations Due to Presence of a Reradiator
80H
SOH
Notes. 1. D (Worst Possible Deviation) is directly dependent upon the lateral and vertical spacings
from the reradiator. 2. A resonant reradiator of Q = 20 has been assumed. 3. For other Q's and
Bon-resonant conditions, see text. 4. Curves show reradiator spacings to maintain constant D or F.
36
34
32
30
28
26
24
22
= 16
14
12
10
8
6
4
2
4 2 4 A
X
T
T
A
4
\
\
T
HX
4
HS.
A
HX:
Base
492
~ FMO
_ 246
~ ^MC
f.et
\ ^
\
\
\
\
\
feet
\
\
\
\
\
\
= -= — feet
jd oo velocity
In air
\
\
s
\
\
\
\
\
\
\
\
\
\
\
\
\
\
\
\
\
N
\
\
\
\
\
\
s
s^
\
S
x,
"^
\
^
v^
^
v^
<^
^
"^^
- — .
0 5 10 15 20 25 30 35 40 45 50 55 60 65
"H" in feet
FIG. 2(6). Fundamental and Harmonic Resonant Frequencies of Conductors of Physical Heights H
ESTABLISHED NAVIGATIONAL AIDS
22-41
added for end effects and top loading as shown in Fig. 2(c). The range of Q's is approxi-
mately as follows:
Wide-width reradiators (superstructures) 1.5-2
Medium-width reradiators (funnels) 2 -3
Narrow-width reradiators (masts) 5 -10
Very thin reradiators (guy wires, antennas) 10 -20
It can be seen from these results that DF antenna locations on top of the tallest structures
give the least reradiation error effect from those structures and, generally, maximum
clearance (least error) from the other, surrounding structures. Breaking up structures
-4V-
}< w ^
Ex. 2 Bridge: <
T
tz -*••* ^— ft -^ Jr-fy
Ex. 3(a) Mast: d<<W Ex. 3(6) Mast with yardarm Ex. 3(c) Mast with loop
Ex. 4(a) Tall mast: eZ«W Ex. 4(6) Tall mast Ex. 4(c) Tall mast
H >W with yardarm with loop v
Note: r shows region of strong reradlated fields
FIG. 2(c). Top Loading and End Effect Corrections for Shipboard Reradiator Heights 17
(e.g., guy wires, rails) with insulators, to reduce the induced currents, further reduces the
environmental effects. Partial compensation of environmental effects can often be ob-
tained by judiciously introducing compensator loops or structures, such that an approxi-
mately equal and opposite (compensating) environmental effect is obtained. Successful
means have been devised for altering the frequency characteristics of structures surround-
ing a DF antenna in order to reduce and control environmental effects. (See reference 5.)
Quadrature effects are generally reduced by minimizing the environmental effects as
stated above. However, in practical direction finders, some polarization effects and resid-
ual environmental effects often leave high values of quadrature effect which must be further
minimized in. order to realize satisfactory DF bearing resolution. Quadrature balance or
compensation has long been used for this purpose. It makes use of a non-directional
antenna for obtaining a voltage from the arriving wave which, with a properly adjusted
phase and amplitude, can be made to cancel out completely the undesired quadrature
voltage derived from the directional collector. In practice, the phase shift, if any, required,
for the above balancing or compensating voltage is a constant value over the frequency
band. As a result, most direction finders operating below 2000 kc/s incorporate this
balance circuit with only a single associated panel control for positive and negative magni-
tude of compensation adjustment. The non-directional antenna employed for balancer
purposes is actually the same one generally furnished in practically all direction finders for
22-42
AIDS TO NAVIGATION
±24-
M
FIG. 3.
(a)
Vector Relations for Quadrature-effect Suppression by Mod-
ulation Method
sense determination, i.e., for resolving the 180° ambiguity in the direction of a received
signal. When used for that purpose, the phase and magnitude of the sense antenna voltage
is adjusted (generally by a fixed circuit) to match (as closely as possible) the phase and
magnitude of the directional antenna's maximum coupling output. In this manner the
cosine (double null) coupling law is converted to an approximate cardioid (single null)
coupling law which possesses the desired single non-ambiguous null. Because the cardioid
law yields a poorer bearing resolution, i.e., differential amplitude to angle ratio, in the
region of its null as compared to the cosine law null region, the cardioid is rarely used for
other than sense determination.
Receiver-introduced modulation for quadrature-effect suppression (see reference 6),
which has recently been developed, possesses several advantages over the balancer type.
It operates on the principle of phase discrimination for the undesired quadrature com-
ponent. Phase discrimination is accomplished by introducing the voltage e\, derived
from the non-directional antenna, into the DF as a reference voltage of proper amplitude
and phase with respect to the directional voltage, e-2. The directional voltage ez is then
passed through a mechanical or electronic reversing switch just before it is added to e\.
The resultant e* has a maximum +es and a minimum — 63 value depending upon the
position of the reversing switch as shown in Fig. 3 (a). It will be noted in Fig, 3(6) that
the undesired or quadrature
directional antenna voltage
component e*', after pass-
ing through the common
reversing switch, is also vec-
torially added to e\. The
resultant e$ thus also has
values +63' and —63' de-
pending upon the position of
the reversing switch. How-
ever, it will be noted that
the desired directional volt-
age ±62 causes a maximum
differential effect on 63, whereas the undesired or quadrature directional voltage ±62'
causes a minimum (zero) differential effect on e$f. Moreover, for small values of quad-
rature, the magnitude of +es' differs negligibly from e\> Thus, if e^ is 10 per cent of e\,
±e3 = V(l)2 + (O.I)2 = 1.005, or the presence of 10 per cent 62' bauses only 0.5 per cent
increase in 63 over ei. By utilizing suitable synchronous commutators, . or sweep circuits
with a cathode-ray tube, the maximum and minimum resultant voltages ±63 can be com-
pared and the desired sharp null position of the collector can be obtained just as readily
with considerable quadrature voltage present as when none is present, since the entire
quadrature suppression is continuous, automatic, and independent of the operator. It
should be noted that positive sense determination is continuously present in this type
of system since the non-directional reference voltage, ei, is automatically a sense voltage,
and sense is obtained merely by correlating the instantaneous position of the reversing
switch with an increasing (or decreasing) resultant output. It can be shown that the
receiver-introduced-modulation principle markedly improves the signal-to-noise ratio
(or the bearing sensitivity) by integrating out the random (non-synchronous) noise effects.
It can be effectively demonstrated that satisfactory DF bearings can be obtained on broad-
cast program modulated signals notwithstanding noise levels that obliterate the program
intelligence. The cathode-ray tube comparator for "on bearing" indication in some U. S.
Navy direction finders is especially desirable for obtaining indication on ICW transmis-
sions. When CW or MOW transmissions are employed the entire DF bearing may be
taken automatically by employing a suitable controlled servo system to orient the direc-
tional collector for minimum difference in H-ea and —63. This identical principle is em-
ployed in the automatic direction finder (ADF) described in article 3 under Aids to Air
Navigation, and as a second mode of operation in the Navy DBD MF/DF system, the
latter being especially designed for simplified marine use. Both the balancing and the
modulator suppression of quadrature effects may, under certain conditions, introduce a
deviation effect. This may occur when a large quadrature (undesirable) voltage, e\ , is
induced in the non-directional antenna. This condition, and its amount, can be quickly
identified by a shift of the reciprocal bearing (i.e., observed bearing plus 180°) from its
normal 180° position. Since this effect is almost identical to, and originates from, the same
mechanisms responsible for the normal Deviation, it is as stable as the latter, and can be
absorbed by the overall DF calibration when made.
Calibration Curves. A conventional DF calibration curve is shown in Fig. 4(a) which
is generally taken for a few of the most received frequencies. The same data can be pre-
ESTABLISHED NAVIGATIONAL AIDS
22-43
sented in the automatic interpolation (see reference 5) form shown in Fig. 4(6) . The latter
form permits more direct plotting and utilization of the calibration data with the great
2? 4-1
r
>
(.
00 1
N
<c ,.
X
"\
X
-^
"° 0
A
V.
/
1 /
/" \
\
^
^
00 k
c
/ /
/^
\
^
c u
\
ss.
s
/
\
s
/
V,.
o-l
\
\ "
/
'•5-2
\
1
\
\
1
/
Q
-3
V
y
^
J
C
)
4
5
9
0
i:
35
It
30
2:
25
2;
rQ
31
5
36
Observed bearing
FIG. 4 (a). Conventional Deviation Chart for Direction-finding Calibration
advantage that the corrected bearing of other than calibrated frequencies may be ascer-
tained just as conveniently as that of the calibrated frequencies.
Polarization Effects. Radio waves propagated with their electric field vertical have
become known as vertically polarized waves; those having their electric field horizontal
D-F calibration Interpolation charts
fore-starboard quadrant
iooh
3551-
1.5
2.0 2.5 3.0
Frequency-megacycles
FIG. 4(6). Automatic Interpolation Chart for Direction-finding Calibration
4,0
have become known as horizontally polarized waves; those having their electric field in-
clined are a combination of both types. Experience shows that most direction finders are
susceptible to appreciable unwanted polarized energy pickup, notwithstanding the care
22-44
AIDS TO NAVIGATION
taken to exclude it from the antenna and feeder system. For a discussion of this effect
and its cure see Section 6, article 32.
WEATHER AND TIME TRANSMISSIONS. Radio navigational warnings and stand-
ard time signals are available to all ships equipped with communication receivers. The
navigational warnings include the local weather forecast plus any urgent information with
regard to tidal waves, offshore winds, ice, and storms.
10. RECENTLY INTRODUCED NAVIGATIONAL AIDS
RADAR. (See references 7-12.) Present radar systems provide one of the few known,
yet most reliable, methods for surface-obstacle detection under conditions of restricted
visibility, whether these obstacles are other ships, icebergs, buoys, islands, landmarks, etc.
Radar provides, in effect, an electronic searchlight aboard ship, capable of "seeing"
through darkness or fog, in any weather condition, for ranges up to approximately 25-30
miles (line of sight), depending on the power of the "searchlight." The use of radar,
therefore, will be most applicable to collision prevention at sea, iceberg detection, harbor
navigation, coastal navigation, and harbor control from shore stations.
Table 2 lists minimum specifications for marine navigational radar. These specifications
suggest the use of PPI (plan position indication) presentation of the echo information
(see Section 15, article 24).
Table 2. Performance Factors for Some Marine Navigational Radars
Performance
Factors
TJ.S.C.G.
Class A Spec.*
Manufac-
turer A
Manufac-
turer B
U.S.C.G.
Class B Spec.f
Manufac-
turer C
Manufac-
turer D
Maximum range. . .
Minimum range. ..
Range resolution
30 miles
100yd
100yd
32 miles
100yd
100yd
40 miles
100yd
100yd
30 miles
400yd
200 yd
30 miles
200yd
100yd
50 miles
100yd
Bearing resolution
4° (on 10 cm)
3°
3°
6°
3°
Presentation
3° (on 3 cm)
1" PPI
7" PPI
12" PPI
1" PPI
1" PPI
7" PPI
Range scales
(miles)
Range acfiUTAcy
2-5, 4-15, and
15-30
±2% or ±50
2, 8, and 32
2, 10, and 40
±2%
2-5, 4-15, and
15-30
±2% or ±100
2, 6, and 30
±2% or ±100
1.5,5, 15, and
50
±2%
Bearing indicator. .
Antenna:
Beam width
Rotation
Frequency
yd
True
4°H, 15°V(on
10 cm); 2° H,
15° V (on 3
cm)
360°, 6-15 rpm
3000-3246
Relative true
(avail.)
2° H, 15° V
360°, 12 rpm
True
2°H, 15° V
360°, 15 rpm
yd
True or relative
5°H, 15° V
360°, 6- 15 rpm
3000-3246
yd
True
5°H, 15° V
360°, 1 1 rpm
3200
Relative true
(avail.)
3.5° H, 12°V
360°, 7 rpm
3070 ± 50
(Me/s)
9320-9500
9320-9430
9320-9430
9320-9500
R-f source
Magnetron
Magnetron
Magnetron
Magnetron
Magnetron
Peak power
15 kw
15 kw
35 kw
7 kw (on 10
7kw
15 kw
Pulse rate
Pulse width
Receiver:
Band width
800 cps
0.5 MS (maxi-
mum)
2000 cps
0.4 MS
800 cps
0.25 MS
8Mcs
cm), 15 kw
(on 3 cm)
800 pps
1 .0 MS (maxi-
mum)
Optimum
1500 pps
0.5^8
Optimum
1000 pps
0.4 MS
3 Mcs
Gain
120 db
120db
117 db
* Class A corresponds to U.S.C.G. Minimum Specifications, Brief No. i; Nov. 14, 1945 (revised Aug. 1, 1946).
t Class B corresponds to U.S.C.G. Minimum Specifications, Brief No. 2, Nov. 14, 1945 (revised Aug. 1, 1946).
Principles. A short powerful burst of electromagnetic energy is emitted at a known
spot and is narrowly beamed in a given known direction. Returning echoes from ob-
jects within an arbitrary range in that given direction are received at the known spot,
detected, and visually displayed. For persistence and continuity of display, the emitted
pulses are repeated periodically at a fixed rate with enough intervening time to allow the
return of any echoes. If an echo from an object is received by the system after a time
delay, T, from the initial burst, the distance of the object from the radar system is:
(3)
RECENTLY INTRODUCED NAVIGATIONAL AIDS 22-45
where c is the velocity of light (or electromagnetic waves) in air and where the time T is
measured from the beginning of the transmitted burst to the beginning of the received
echo. Thus, the distance to the object is determined. If the antenna system is sufficiently
directive, the pointed direction of the antenna at the time an echo is received is the direc-
tion of the echo, thus furnishing a bearing determination.
^ Unless the wavelength of the radiations used is small compared with the linear dimen-
sions of the reflecting object, the phenomenon of diffraction takes place, making the echo
amplitude inversely proportional to the square of the wavelength. If the wavelength is
small compared with the reflecting object, the amplitude of the echo field does not sensibly
depend upon the magnitude of the wavelength but rather upon the nature of the reflecting
object. In the case of the free-space propagation between the radar system and the
reflecting object, the following relationship holds:
where Pr is the received power at the receiver input terminals (watts), AQ is the effective
absorption cross-section of the receiving antenna (square meters) , Go is the overall power
gain of the feeder and the radiating antenna, Pt is the transmitter peak power (watts), K
is a complex reflection coefficient dependent on the nature of the target and is given as
the effective echo area of the target in the direction of the radar (square meters) , r is the
distance in meters from the radar to the target. The second form of the equation is in
terms of the maximum range, rmax., and the minimum detectable power received, Pmin.-
These results for free space propagation must be modified for propagation over a spherical
earth since, in the range of frequencies used, electromagnetic waves are propagated over
approximately a "line of sight" path with small diffraction effects occurring at the lower
radar frequencies. Thus, the antenna height above the sea, the target height above the
sea, and the height of any intervening objects must be taken into account.
From these considerations, it is evident that, in order to utilize efficiently the principles
of reflection with electromagnetic waves, a radar system must (1) generate a wave whose
length is small compared with the objects from which the wave is to be reflected; (2)
generate enough power at that frequency to be able to receive and detect the returning
signal; (3) provide a means of measuring the tune delay from the transmission to the recep-
tion of that signal.
Fundamental System Constants. Each radar system has associated with it certain
constants whose choice depends upon the available components, the desired operational
performance, and the intended use of the system. The normal variations of these constants
are as indicated in the following:
(a) Carrier Frequency. The choice of carrier frequency depends on the permissible
dimensions of the antenna system to -be used and the directivity or beam sharpness desired,
since the size of the antenna system reduces with increased frequency, and the directivity,
as well as gain, improves with frequency for a given antenna size. Thus the lower fre-
quency is limited by the practical antenna size; the upper frequency is limited by atmos-
pheric reflection and absorption effects (pronounced near 3000 Me or 10 cm wavelength
for reflection and 30,000 Mc/s or 1 cm wavelength for absorption) and the availability of
tubes capable of generating and amplifying enough radio-frequency energy to provide
the necessary range. The lower frequency limit is about 100 Me, though frequencies higher
than 30,000 Me have been successfully used experimentally.
(6) Transmitter Pulse Width, The minimum range at which an object can be detected
by a radar system is determined largely by the width of the transmitted pulse (at the
x/2 power point) since an echo returning while the transmitter is still operating will be
masked by the transmitter pulse. This is even more true if the receiver is always blocked
or desensitized for the duration of the transmitter pulse. The usual pulse widths range
from 0.25 to 2.0 /-is for navigational purposes.
(c) Pulse Repetition Rate. The pulse repetition rate must be slow enough to allow time
for the maximum range echoes to return to the antenna before another pulse is transmittedf
and it must be fast enough to provide enough traces while the antenna is rotating or
pointing in a given direction to produce a lasting indication on an oscilloscope screen.
Therefore the maximum range determines the highest pulse rate, and the rotational speed
of the antenna determines the lowest pulse rate that can be used. In practice these rate*
vary from less than 60 to several thousand pulses per second.
(d) Duty Cycle. The duty cycle of a radar system is the ratio of the average power to
the peak pulse power. It depends on the relation between pulse width and the pulse-
repetition time. Thus a lower duty cycle permits higher peak power operation at the same
average power. The maximum range of the system is dependent on the peak power for a
given pulse width, while low average power means smaller tubes and components ia the
22-46
AIDS TO NAVIGATION
,-Awir-
transmitter. The limit to peak power, however, for a given transmitter tube is the break-
down potentials between the various electrodes. In practice, radar duty cycles vary
between 0.005 and 0.0001.
Fundamental System Components (General). Radar systems now in existence differ
-widely in detailed design and complexity, depending on their functional use and the accu-
racy and amount of information required. However, a single basic system can be visualized
in which the functional requirements fit equally well almost all specific requirements.
The six primary components are shown in Fig. 5; they may be summarized as follows:
(a} Timer or Synchroniser. The timer determines the pulse-repetition rate of the radar
and provides a zero reference point for time measurements and for operation of sequential
functions in a definite time relationship. Such timing may be supplied by a separate unit
such as a sine-wave oscillator,
T y a multivibrator, or a blocking
oscillator with the necessary
pulse-shaping circuits. An-
other commonly used method
of timing is to make the
transmitter with its associ-
ated circuits establish its own
repetition rate and provide
the synchronizing pulses for
the rest of the system. This
action may be accomplished
by a self-pulsing or blocking
radio-frequency oscillator, or
by a rotating spark gap.
Self-timing eliminates a num-
ber of special timing circuits,
but the pulse width and pulse-
FIQ. 5. Functional Block Diagram for Basic Radar System
repetition rate are not usually as stable or rigidly controllable as is necessary for some
applications.
(b) Transmitters. To generate pulses of high-frequency electromagnetic waves at high
power levels a conventional pulse transmitter is used. Care must be taken that the tubes
are suitable not only for the average power dissipation but also for the high powers and
voltages during the pulse.
(c) Antenna System. The purposes of the antenna system are to beam and radiate the
energy efficiently from the transmitter into space, to focus and pick up the returning echo
and pass it on to the receiver. A transmit-receive switch (TR box) must be included to
prevent the transmitter energy from harming the receiver.
(d) Receiver. A conventional wide-band receiver is used.
(e) Indicator. To display the detected pulses visually so that range, bearing, or eleva-
tion of any echo source, or combination of these, can be determined. See Section 15,
article 24.
(/) Power Supply. A conventional well-regulated low-impedance power supply is used.
Pulse-forming lines build up a charge during the inactive period to store energy to discharge
in the pulse.
Performance Factors, (a) Resolution. The resolution of obstacles by a radar system
will depend on the pulse width, the effective antenna beam width, the receiver band width,
the frequency, and the stability of the entire system. For a typical commercial naviga-
tional radar in the 3-cm (10,000-Mc) band, having a receiver band width of 8 Mc/s,
antenna beam width of 2° (to half power points), and a pulse width of 1/4 //s, the resolution
is 100 yards in range and 3° in azimuth. Above approximately 1000 Mc/s the frequency
is not a major determining factor in itself, but only as it affects the other factors, since the
•wavelength is small enough to provide efficient reflection from the smallest objects ordi-
narily encountered.
(b) Maximum and Minimum Range. The maximum range will depend on the height of
the antenna system above the sea, the power output of the transmitter, and the gain and
efficiency of the antenna system. An average ship installation would have a maximum
range of from 25—30 miles, which is, in general, great enough for the intended navigational
use. - The minimuin range will depend directly on the pulse width and recovery time of
the receiving system (including antenna switching mechanism) ; for the typical commercial
system mentioned above, it is 100 yards. The radar indicator is usually provided with a
range switch permitting any of several discrete ranges to be displayed on the screen. The
accuracy of the range information depends on the initial accuracy and stability of the range
markers; azimuthal accuracy usually depends on the accuracy of tracking between the
RECENTLY INTRODUCED NAVIGATIONAL AIDS 22-47
antenna rotation and the sweep rotation on the cathode-ray tube face. Accuracies of
2 per cent in range and 2° in azimuth are not unusual.
(c) Presentation. The most usable form of the radar information for marine navigational
purposes is the PPI type presentation on a screen of 5 to 9 in. in diameter, with provision
for true or relative bearing stabilization, range markers, and range scale selector. The ratio
between different range scales is often made the same.
(d") Installation, Maintenance, and Operation. The present radar systems are designed
for operation by bridge personnel having little or no technical training. The indicator is
mounted in the pilot house, and the antenna is properly located to provide 360° clearance
to the horizon. To facilitate this arrangement on all types of vessels, the radio-frequency
components, the antenna assembly, and the indicator are usually manufactured as separate
units.
RADAR-BEACONS (RACON). (See references 10-12.) Radar piloting is beset by two
important problems. First, targets for navigational purposes are sometimes small or
poorly denned, resulting in small or weak echoes, especially near the maximum range of
the radar system. Secondly, these weak echoes in the presence of sea return often
leave the absolute identification of the navigational targets in doubt. These prob-
lems are greatly simplified, however, by providing a system of electronic beacons designed
to serve as aids to navigation for ships equipped with the proper radar equipment. The
term Racon, a contraction of radar-beacon, designates such a system. These beacons or
racons are designed to emit or reflect a large amount of energy which will allow dependable
target indication at a much greater distance than that obtainable when normal reflections
alone are depended upon. There are three types of such beacons, and each is described
below:
Radar Respondor-beacons (Transponder). These racons consist of transponders, or
pulse-type receiver-transmitters, located at strategic ground sites such as coastal points
and islands, which receive
interrogating signals from
a radar transmitter and
automatically send back
identifying reply pulses to
the radar. The coded reply
appears on the radar oscil-
loscope in such a way that
both position and identifi-
cation of the racon station
are indicated. Reference to
prepared code lists or charts
then serves to associate that
respondor-beacon with a
fixed navigational point.
Thus a navigator will be
able to check his course, or
even completely guide his
craft, since range, bearing,
and identification will be ob-
tained from each respondor-
beacon. A typical radar
and fixed station microwave
Receiving
antenna
Transmitting
antenna
Functional Block Diagram of Basic Racon System
racon transpondor operation is shown in the block diagram in Fig. 6.
To prevent racon signals from appearing on the radar screen all the time, and to avoid
continual interrogation of the beacon by radar, the system is designed to operate under
the following conditions: (1) the beacon responds only to pulses of 2-jus or greater duration
within an appropriate frequency band; (2) the beacon replies at a fixed frequency which is
common to the entire beacon system and which is just outside the radar system frequency
band. Ten-centimeter band racons respond to 2-/zs challenging pulses in the 3000-3246
Mc/s band and reply at 3256 Mc/s; 3-cm band beacons receive pulses in the 9320-9500
Mc/s band and reply at 9310 Mc/s. An additional band near 5 cm is being made available
for radar and racon use. For racon system use, the radar equipment is designed to provide
the necessary challenging pulse length and the correct receiver tuning upon activation
of a special button or switch. The normal radar plot will then disappear and only radar-
beacon responses will appear on the screen.
Three types of coding, to insure positive identification of a given respondor-beacon,
have been devised: (1) Sequence coding is provided by emitting a number of half-second
transmissions whenever the beacon is triggered. During the half second, pulses of a given
22-48 AIDS TO NAVIGATION
duration appear as a pip of a certain width on the scope. However, the pulses making up
the next transmission may all be of longer duration, thus giving a pip of greater width on
the scope. The complete code is made up of the number and combination of widths of
these pips. (2) Gap coding provides periodic interruption of a series of pulses. During
each period of interruption, identification is given by a pulsed dot and dash transmission.
Both sequence and gap coding are slow, requiring considerable time for complete identi-
fication. (3) Range coding gives an immediate identification as the complete code is
produced on the oscilloscope at once. Each reply, caused by one interrogation pulse,
consists of six pulses which appear on the PPI at different positions along a given bearing
with the first pulse indicating the beacon position. Such coding is accomplished by chang-
ing the spacing of the pulses.
Separate broadside arrays serve as receiving and transmitting antennas for the trans-
ponder. Both are non-directional in the horizontal plane in order to respond to interro-
gations from any point on the compass, but have a narrow low-angle vertical pattern to.
facilitate long-range operation. From the receiving antenna the received radar signals
go to either a crystal-video or superheterodyne receiver which must satisfy the follow-
ing requirements: (1) the radio- and intermediate-frequency stages must be broad-band
in order to receive signals at any frequency within a given radar band (10-cm or 3-cm, but
not both); (2) the video stages must not excessively widen 1-jus radar pulses; (3) the re-
ceiver must not be easily blocked; (4) the amplification must be adequate for the received
radar signals. The output of the receiver goes to a recoder which consists of a discrim-
inator, coder, and gate multivibrator. The discriminator accepts variable amplitude-
pulses of 2-/IS or greater duration but rejects all pulses of shorter duration. The coder
(in this case, a range coder) consists of six start-stop multivibrators whose outputs are-
combined in an amplifier to produce a series of pulses. The code may include a maximum
of six pulses with 15- or 35-Ats spacings between successive pulses. The gate consists of a
175-jus negative rectangular pulse that is fed back to the discriminator, where it prevents
the coder from accepting other receiver video signals until after the completion of one
range-coded transmission. The pulses from the coder are applied to a modulator where
they are converted into very large amplitude rectangular pulses of Va-MS duration. The
modulator triggers a transmitting magnetron that oscillates at the proper reply frequency.
To insure operation exactly on the radar transmission frequency, an automatic frequency
control circuit is used to keep the magnetron in tune. Minimum peak powers of 10 kw
are used, while some racons operate at peak powers as high as 40 kw.
Transponder beacons of the type described, and radar equipments which use them,
must be designed as "sister" equipments, as each is dependent upon the other. For this
reason the Coast Guard's specifications for commercial radar equipment recommended
that provisions be made for convenient future modifications of the radar for use with racons
or microwave beacons. Considerable investigation and development work has been under
way to permit adaptation of the wartime racon system to general marine navigational
purposes.
RADAR MARKER BEACONS (RAM ARK). A second type of radar beacon consists
of a simple shore-based, continuously pulsed beacon operating on a single frequency.
Rather than being interrogated by the radar pulses, this type continuously transmits,
and the radar need have only a means for receiving the beacon frequency when it is desired
to utilize the beacon. This eliminates the necessity for sending out 2-jus pulses and simpli-
fies the ground equipment so that it acts in much the manner of the present low-frequency
radiobeacons. The navigator sees, on his PPI, a line extending radially from the center to
the periphery of the scope on the bearing of the beacon. Two beacons are needed to obtain
a fix since no range information is provided. The means of identification is the location
of the aid with respect to the naturally distinguishable land contours shown on the radar.
Additional means of identification have been considered also, e.g., groups of pulses, known
repetition rates, or modulation of the signal with an audio code, but these require addi-
tional modifications to the radar.
RADAR REFLECTOR BEACONS (CORNER REFLECTORS). A third type of beacon
classed as a racon is the "corner reflector," which is merely a mechanical assembly of
sheet-metal faces, designed to give the maximum reflection of energy received from any
given direction over fairly wide angular limits. The reflector is inexpensive and easy to-
construct and maintain. These devices have no means of identification other than their
prominent echoes on the radar screen and the fact that their positions can be plotted on.
charts. The great simplicity and economy of such a scheme suggest its use wherever
feasible. In rough weather, however, it may be very difficult to distinguish its return
through the ground clutter.
LOR AN. (See references 11, 13, and 14.) The accelerated development of radar and
other electronic equipments during World War II has reduced to relatively simple opera-
RECENTLY INTRODUCED NAVIGATIONAL AIDS 22-49
Loran line of position,
(hyperbola of constant
time difference^ 800 jus)
tional procedures the accurate measurement of radio transmission propagation time. This
has resulted in the introduction and wide use of two important radio position-determining
systems utilizing this propagation time principle, i.e., Loran and Gee. In these systems, a
position fix is obtained from the intersection of two loci of position, each locus of position
being determined by measuring the propagation time difference between two synchronized
pulsed signal emissions arriving from two known but widely spaced radio transmitting
sources. Since the velocity of propagation of radio waves over the earth's surface is
essentially constant, propagation-time-difference measurement varies directly as the
distance difference between a receiving station and two fixed transmitters. Therefore,
the locus of points which are a given constant time difference from two fixed points is a
hyperbola with the fixed points as foci. Thus the two transmitting stations or fixed points
provide a family of hyperbolas about the stations, each hyperbola representing a constant
value of propagation time difference. Position-fixing methods which use such a family of
hyperbolas can be classed as hyperbolic systems, and, in addition to Loran and Gee, they
include the Dingley system, Decca, and Popi. These last two systems utilize hyperbolas
derived from constant propagation phase differences (identical in principle to optical
interference phenomena) instead of constant propagation time difference, whereas the
Dingley system utilizes hyperbolas derived from constant propagation frequency differ-
ences.
STANDARD LORAN. This system operates at approximately 2 Mc/s and utilizes
ground wave and/or single hop E layer paths of transmission. Special charts are provided
having Loran hyperbolas super-
imposed on geographical maps.
Figure 7 shows a partial exam-
ple of Loran hyperbolic charts.
In practice, a master (or A) sta-
tion transmits 40-^s pulses at
a given repetition rate. These
pulses serve to synchronize a
slave (or B) station several hun-
dred miles away so that the B
station also transmits 40-/^s
pulses at the same repetition rate,
but delayed in time by the travel-
time between the two stations
plus the B station's system delay.
The reception and presentation
of these transmitted pulses
aboard ship by means of a special
Loran receiver and indicator
permit measurement of their
time difference, and from that in-
formation the appropriate Loran
chart will give the correct corre-
sponding hyperbolic line of posi-
tion. A separate operation on a second pah* of Loran transmitting stations provides a
second position curve, and the intersection of these hyperbolic curves on the special charts
establishes a "fix." A block diagram of the Loran system is shown in Fig. 8.
Transmitting Equipment. The Loran transmitting stations generally operate as a
group of four stations. Each station would normally consist of a timer and a transmitter.
The timer establishes a very precise pulse rate by utilizing 50 kc/s or 100 kc/s crystal-
controlled oscillations of very high accuracy, which are divided down to provide basic
pulse rates of 25 pps and 33 Vs PPS. These timing pulses trigger an exciter which generates
the 40-/ZS pulses for modulating the transmitter. The transmitter itself is a self-excited,
tuned-grid, tuned-plate, push-pull unit, pulse modulated in the cathode circuit and
oscillating from 1750 to 2000 kc/s. To provide precise synchronization, to conserve
equipment, and to reduce maintenance, a single transmitter is usually employed as a
master station which synchronizes two different slave stations, on the same frequency,
but at different repetition rates. This is accomplished by providing, at the transmitter,
two separate timers (each of which is independently referenced, for convenience, to the
precise time signals from station WWV), two exciters, and a mixer stage preceding the
modulator. The duty cycle of this double-pulsed transmitter system is approximately
80 fj.s in every 40,000 /zs (25 pps), or 0.2 per cent. The transmitter, operating at about
100 kw peak power, feeds a 120-ft guyed radiator in the standard installation. In case of
damage by windstorm, etc., an emergency T antenna is provided. The slave-station
FIG. 7. Loran Hyperbolic Line of Position
22-50
AIDS TO NAVIGATION
emitting equipment is identical to that of the master station, and suitable means are
provided at the slave station for properly receiving the master station signals and for
effecting the necessary precise synchronization of the slave-station pulses.
Major components of
Loran receiver
Major components of
double pulsed Loran
master transmitting station
FIG. 8. Functional Block Diagram of Basic Loran System
RECEIVING EQUIPMENT. The craft's receiver-indicator equipment is usually
furnished with a 50- to 60-ft vertical antenna leading to a medium-frequency receiver
having a band width of 50 kc/s to pass the 40-Ais pulses, and a 50-kc video output stage.
To insure maximum range reception, the receiver must have enough sensitivity and gain
to provide full screen deflection with 10 microvolts into the receiver. The indicator pro-
vides the necessary timing circuits to measure pulse separations with the required I-AIS
precision. A 100 kc/s precision oscillator with associated dividers supplies a sequence of
precise index timing markers at appropriate intervals, with a basic accuracy of dbl us. It
also contains the delay and deflection circuits for displaying the received pulses or the
timing markers on the oscilloscope screen. The actual method of presentation is to pro-
vide separate paralleled sweep traces on the scope screen, one for the train of A station
pulses and one for the train of B station pulses, with the index markers appearing simul-
taneously on the screen with the station pulses. Since more than one Loran transmitter
may be operating on the same carrier frequency, pulses from all these stations will appear
on the indicator screen. Therefore, the indicator includes timing and sweep circuits which
provide precise repetition rates corresponding to the desired transmitter's repetition rates.
This procedure synchronizes the indicator to the pulses of only one transmitting pair of
Loran stations while the pulses of all others continuously drift across the screen and do not
interfere with the desired stationary pair of pulses.
The exact amount of time delay between the slave and master pulses can be measured
from manually incorporated time delay circuits required to make both these pulses coincide
on the screen. The accuracy of measurement depends on the stability of the circuits which
provide timing markers on the face of the oscilloscope. To facilitate this, an expanded
or fast sweep is provided, enlarging the picture of the pulses and making the pulse-matching
procedure accurate to approximately I-MS, since the 10-jus marker spaces can be estimated
to tenths. A typical presentation is shown in Figs. 9 (a) and 9(6). A receiver refinement
introduced by the Sperry Gyroscope Company permits the local time delay (equivalent
to the time difference) to be read directly in microseconds on a Veeder-type counter. The
currently available shipboard receiver-indicator equipment weighs between 125 and 235
Ib, although the corresponding airborne equipment is a comparatively small unit weighing
approximately 25 Ib. Both types consume 200 to 300 watts from a 115- volt power source.
RECENTLY INTRODUCED NAVIGATIONAL AIDS 22-51
One-hop-E
Performance. When used over water Loran can provide navigational fixes up to 750
nautical miles in the daytime and up to 1400 nautical miles at night. The daytime range
is the limit of ground-wave propagation at the frequencies and power used. At night,
pronounced reflection effects from the E layer of the ionosphere provides the additional
range. Fortunately, this ionospheric reflection introduces only small errors which are
compensated by known correction factors and allowed for in the Loran charts. When the
ship is in a position to receive both ground- and sky-wave transmission, the indicator
will show two or more sets of pulses where the first set is the ground-wave pair and the
others are various sky-wave reflections as shown in Fig. 9 (a). Such reception does not
interfere with the fix determinations. The average operating accuracy of present systems
is better than 0.5 per cent of the distance measured, e.g., less than 31/3 miles in 500 miles,
but deteriorates somewhat along the base line of the transmitters. The accuracy depends
on the location of the trans-
mitting stations, the stabil-
ity of the timing circuits,
and the experience of the
operator in matching pulses
and estimating time be-
tween 10-/XS markers.
Since the system depends
upon the measurement of
time differences rather than
upon direction of propaga-
tion, it is not subject to
the usual errors encountered
in direction-finder systems.
Factors affecting the propa-
gation from a master station
will, in general, also affect
the propagation from its
slave station. This is espe-
cially true as the range in-
creases, since the two paths
then become approximately
parallel. At the close of the
war, the military Loran sys-
tem comprised 40 trans-
mitting stations located at
strategic geographical
points, with an additional
10 under construction;
these systems supplied in-
FTG. 9 (a). Typical Ground Wave and Sky Wave Pulse Sequence
from One Station. Signals to the right of the One-hop-E are gener-
ally disregarded.
FIG. 9(6). Basic Loran Indicator Pattern. A calibrated time differ-
ence (or delay) mechanism and an expanded sweep are used to obtain
1 microsecond accuracy.
formation to receiver-indicators installed on more than 3000 surface vessels. Among
the improvements which are desired and may be expected in the near future are the follow-
ing: (1) higher-power transmitting stations (about 1000 kw), (2) crystal-controlled oscil-
lators to provide more stable carrier frequencies, (3) different methods of station synchro-
nization and pulse-shaping circuits, and (4) a totally automatic receiver-indicator system
requiring a minimum of technical operating skill and experience. These improvements
are desired in order to overcome the present disadvantages of: (1) limited range, especially
in the daytime, (2) the undesired synchronization upsets caused by ionospheric disturb-'
ances, (3) the need of a specially trained operator for interpretation and maintenance.
In addition, experimental studies are being conducted (see below) on LF Loran which is
an adaptation of standard Loran to the very low-frequency range.
SS LORAN. This system (sky-wave synchronized Loran) is operable during the night
only and is identical to standard Loran except that master and slave stations are sepa-
rated by 1000 to 1200 nautical miles instead of the usual 200 to 300 nautical miles. Such
a long base line requires synchronization of master and slave stations by sky waves, since,
at the operating frequency of 2 Mc/s, the range of the ground-wave propagation is less
than the base line itself, so that SS Loran can be used only at night, when sky waves are
strong.
LOW-FREQUENCY LORAN. To provide greater daytime range, a modified Loran
system has been designed which operates at about 180 kc/s and offers the following propa-
gation advantages: (1) at these low frequencies the propagation range of ground waves is
increased, especially over land; and (2) sky-wave reflections become much more stable,
to' such a degree that they can more readily be interpreted by a navigator. ™~ **oWi^r
This stability
22-52
AIDS TO NAVIGATION
results from the fact that radio-frequency energy at these frequencies does not penetrate
the E layer of the ionosphere and thus the long trains of multiple night time sky waves,
present at 2 Me, are absent. Hence, the 180 kc/s sky-wave receptions are much more
useful to the operation of the Loran system and it appears possible to obtain ranges of
1000 or more miles for satisfactory, stable operation for day or night over land or sea.
However, resolution (separation) between the ground-wave and various sky-wave recep-
tions deteriorates and affects the accuracy of the system. At very low frequencies (below
180 kc/s), ground waves are even less attenuated, and very reliable propagation over
thousands of miles can be expected. However, because very wide-band antenna systems
are not available at the very low frequencies in view of their prohibitive size and because
of current limitations of wide-band and pulsed techniques, the pulse principles inherently
required in Loran have not yet been adapted to the very low frequencies employed. In
view of these factors it seems that 100-150 kc/s is about the lowest usable frequency range
in which pulsed systems such as Loran can be employed, with the pulse length increasing
to about 300 jus.
GEE SYSTEM. The British Gee system of navigation operates in the 20-85 Mc/s
frequency range, on the pulse-propagation-time-difference principle. In nearly all respects
it is the higher-frequency counterpart of the Loran system and was independently de-
veloped by the British. The essential differences of the Gee system are: (1) higher operat-
ing frequency and consequent reduction of range ; (2) three-slave-station operation instead
of two; and (3) simultaneous presentation of two propagation time differences in order
that a position fix can be determined in one initial receiver operation.
CONSOL (BRITISH) AND SONNE (GERMAN). (See references 15 and 16.) Consol
or Sonne is proposed as a medium-range navigational aid of the rotating beacon class.
Radio navigational aids of this class operate in much the same manner as a directional
searchlight which revolves at a known and constant rate with the addition of a non-
directional visual light signal marking the instant that the revolving light passes through
true north. The observer, at the point where the line of bearing to the beacon is to be
determined, needs only to employ a stop watch to measure the time interval between the
reception of the non-directional light signal and the searchlight signal, after which the
desired azimuth angle is computed from the product of the known angular rotational
speed and the time interval. In the Consol system dots and dashes are put into the
rotating antenna pattern so that a stop watch is not needed. The observer simply counts
the number of dots and dashes between the "north" pulse and the equisignal, and obtains
his azimuth from the station thereby. A variation of this rotating-beacon principle
consists of directly imparting the desired azimuthal information to the light beam proper
via correlated modulation methods, e.g., by coding, intensity modulation, or frequency
modulation. Completely analogous rotating radio beacon systems have also been used.
For low and medium frequencies, large rotating antennas, or fixed antennas (e.g., Adcock
type) with rotating goniometer arrangements transmitting a cosine-law or cardioid pattern,
have been used. In other systems a cardioid or cosine-law modulation pattern has been
transmitted, utilizing a receiver with a pattern synchronized cathode-ray sweep for an
automatic indicator. Generally, radio frequencies in the VHF and UHF regions have
been favored because rotating antennas of reasonable dimensions can be more conveniently
built to give the desired sharpness of beam
width to the predominantly single lobe ra-
diation pattern usually employed. The
necessarily high carrier frequency of these
systems unfortunately limits them to line-
of-sight ranges. Consol or Sonne, on the
other hand, is a rotating-beacon system
that operates in the 200-500 kc/s band
and provides an accurate medium-range
facility. Use is made of an ingeniously
employed rotating multilobe radiation
pattern such that sharp bearing resolu-
tions are realized at these ranges.
SHORAN. (See reference 17.) The
Shoran, or short range navigation, system
operates on the principle of echo ranging
on two spaced beacons of the radar-
respondor type. It combines the accuracy
of propagation-time measurement with
FIG. 10. Functional Block Diagram of Basic Shoran simplicity of operation and reliability of
System equipments.
Transmitter
Ft
Receiver
CONTEMPLATED AND PROPOSED NAVIGATIONAL AIDS 22-53
Briefly, Shoran position "fixing" requires the measurement of the round-trip trans-
mission times, in terms of range or distance, of two sets of short radio-frequency pulses
transmitted by the craft, each set interrogating a known shore radar respondor-beacon
station which retransmits the pulses back to the craft. Since each echo range defines an
arc of fixed radius from each known radar respondor-beacon position, the intersection of
these arcs determines the craft's location. The resulting double ambiguity, as in Loran
and Gee, can usually be easily resolved. The two sets of pulses are transmitted from the
craft on separate frequencies as shown in Pig. 10. Upon interrogation, both ground
beacon stations retransmit on a common frequency that is different from either of the
.signal frequencies radiated by the craft. The returned pulses are then received and dis-
played by the craft's equipment. The crystal-controlled repetition rate is the precise
yardstick in terms of which the craft to respondor-beacon distances are measured, and all
interrogating transmitters use this same repetition rate.
DIRECTION-FINDER SYSTEMS (HF-VHF-UHF). (See references 18, 19, and 20.)
Until recently direction-finder systems at these frequencies were quite unreliable. Pri-
marily, this poor operation has been caused by resonant reradiation from structures near the
DF collector. Since a grounded metallic structure will resonate approximately as follows:
/ 246 rn
/(Mc/s) = TTT- (5)
structures between about 8 ft and 165 ft high will have a resonance somewhere in the 1.5 to
30 Mc/s frequency band. (See Environmental Effects, p. 22-39.) On the basis of these
analyses shipboard HF/DF can now be installed with average errors of 5-10°.
In view of their poor accuracy compared to the 1° to 2° shipboard MF/DF accuracy,
it is not likely that shipboard HF/DF will be widely employed for other than military
intercept and location applications.
Shore stations (see reference 20) of 100 Mc/s direction finders employing a vertical
spaced Adcock collector, a spinning goniometer, and a cathode-ray-type automatic indi-
cator have given a 2-3° accuracy with line-of-sight range. At 8 Mc/s planes have been
tracked from the United States to Northern Africa. For the ultra high frequencies 90 to
5000 Mc/s systems use a spinning reflector-type collector (dish) system in lieu of the fixed
Adcock and goniometer arrangement. In general these are not too efficient in the 90 to,
say, 200 Mc/s range but rapidly improve for the higher frequencies.
SONAR. (See references 21 and 22.) Sonar, or sound navigation and ranging, which is
the field of underwater sound navigation, has been applied in a manner similar, in principle
and in electronic circuits, to radar in the field of radio navigation; the principal difference
is the medium of propagation. The two main types of underwater sound aids in use are:
(1) the vertical projectors called echo sounding or depth finding aids; and (2) the horizontal
projectors known as echo ranging units.
Echo sounding equipment transmits sound pulses vertically downward from a projector
placed in the bottom, of the ship, or lowered from the side of the ship, and receives the
reflected pulses from the bottom of the ocean or waterway, giving a direct and constant
running record on graph paper of the depth of water beneath the boat's keeL Present
commercial equipment has a range of 1000 fathoms or less and is used to navigate channels,
rivers, and other waterways and to obtain data for charting the depths of these various
waterways. Information necessary for the plotting of charts having contour lines of
constant depth is gathered by the Coast and Geodetic Survey and is published by the
Navy Hydrographic Office as an aid to marine navigation. This type of equipment has
also been successfully used by fishing boats to locate schools of fish, as they also reflect
sound pulses.
Echo ranging equipment transmits sound in a pattern which is eonically beamed. It
.searches in the horizontal plane from a projector which can be rotated through 360°.
•Originally, the term Sonar implied the use of ranging equipment only, but it now designates
almost any type of underwater sound equipment regardless of its use. This equipment
was originally developed for the U. S. Navy for detecting submarines and surface ships,
but it can obviously be used in the same manner for navigational and anticollision purposes.
It presents the distance from the ship to an object, directly in yards, on a cathode-ray
range indicator, and the bearing of the object with respect to the ship's position on a
bearing indicator compass.
11. CONTEMPLATED AND PROPOSED NAVIGATIONAL AIDS
LANAC. The Lanac or Zaminar navigation and anticollision system is a method of
.electronic navigation, developed since the close of the war, which proposes a unified radar
22-54
AIDS TO NAVIGATION
1
1
1
I
1 Transmitter
I—
1
1
j
Challenger
1 Receiver
1
1
1
,_ _
Indicator
and identification navigational system for both marine and air use (see article 6),
utilizing a minimum of equipments. The Lanac system provides garget identification,
coded radar beacon, and radar search operations from the same basic equipment. Essen-
tially, the proposed system comprises a challenger and a replier, operating at approxi-
mately 1000 Mc/s, as shown in the block diagram Fig. 11. The challenger can also be
operated as a low-power search radar, for auxiliary navigation and anticollision protection.
The repliers are coded for identifica-
tion and (in air use) for altitude dis-
crimination. Thus the system pro-
vides the essential advantages of radar
navigation, but the technical and
operational emphasis is placed on the
beacon operation, which provides pos-
itive point identification of all stra-
tegic locations and other ships,
assuming that the ships are properly
equipped. Thus, for maximum effi-
ciency of operation, most other ships
and prominent geographic locations
would have to be marked by respond-
or-beacons (repliers). The display of
beacon replies on a PPI scope as a
two-dimensional polar plot of the area
surrounding the challenger is easier
and more reliably interpreted than a
corresponding radar display.
A chart of the marine services ren-
dered by Lanac is shown in Fig. 12
with the addition of the auxiliary
radar functions mentioned. Although
1
1
"I
|
Receiver
i
1
r
i
Repfler
1
"1
1
Transmitter
u
i
1
1
1
Identity
Coding
i
J
FIG. 11. Functional Block Diagram of Basic Lanac
System
not yet in general use, Lanac offers the advantages of a simple and very comprehensive nav-
igational aid which combines the reliability of beacon operation with the versatility of radar.
DECCA. (See reference 16.) The British Decca system operates in the low- and
medium-frequency ranges (i.e., 10-200 kc/s) on the propagation phase difference principle
(e.g., similar to POPI). Operation is accomplished by transmitting CW signals from a
master and a remote slave station accurately synchronized so that there is set up in space a
stable interference pattern of radiations having distinct loci of constant phase difference.
/ Danger-ground
buoy beacon
FIG. 12. Summary of Services Rendered by Lanac (Excluding Radar)
These Decca loci are hyperbolas of constant propagation phase difference, as compared
to the Loran loci which are hyperbolas of constant propagation time difference. To facil-
itate the reception of the two distinct transmitted signals, and the practical measurement
of their phase difference, the Decca master and slave CW emissions have a highly stabilized
ratio of carrier frequencies; e.g., the master station may operate on 340/4 = 85 kc/s, the
slave station on 340/3 = 113.33 kc/s. The received frequency ratio is converted to unity
by suitable multipliers in two channels of the receiving equipment. The actual phase
CONTEMPLATED AND PROPOSED NAVIGATIONAL AIDS 22-55
difference between the two signals is then measured by passing the two converted signals
through phase discriminating and indicating circuits. An integrating phase-meter (called
a decometer) numerically identifies each hyperbola of 0° phase difference as it is picked up
by the receiver. These 0° phase difference hyperbolas are called "equiphase" lines and
are used as a reference. All other hyperbolas within the "lanes" between the equiphase
4 lines are then identified on the decometer as values of phase difference other than 0°.
Since two such position lines are required for a "fix," another such phase comparison
determination is necessary on a second pair of stations. The total equipment, therefore,
comprises three shore transmitters (one master operating two slaves) together with their
associated control circuits, and craft equipment consisting of three phase-stable amplifiers,
four frequency-multipliers, and two integrating phase-meters.
In order to avoid ambiguities of fix in the Decca system, the decometers must be preset
to a given reading at a known point which is within reception range of the Decca trans-
mitters. Then, as long as the transmitters and the receiving equipments are operating,
the decometer will read correctly as the receiver travels from one lane to another. If
either the receiver or any of the transmitters fail to operate properly, or the receiver travels
out of reception range, the absolute setting is lost and must be reset at a known position.
To reduce these possibilities of ambiguity, means for positive lane identification are now
being developed, A Decca facility (utilizing four stations centered near London, England)
is in continuous 24-hour operation. Other Decca facilities are being planned including
some for the European continent. The Decca system is easier to operate than the Loran
system and appears capable of giving fix information with greater accuracy, but at de-
creased range. However, errors due to serious phase shifts may be introduced by iono-
sphere reflections of sky wave. It is to be noted that three carrier frequency channels are
required for a position fix with, the Decca system.
POPI. (See reference 16.) The British POPI or post office position indicator system,
operates in the medium-frequency range on the propagation-phase-differenee principle
(similar to Decca) with such a short base line that the hyperbolic lines of position are
essentially straight lines or bearing lines of position to each POPI station. Two or more
bearing lines of position from two or more POPI stations give the desired position fix.
Each POPI station employs three outer antennas symmetrically disposed about a central
antenna. If the antenna spacings are equal to or less than X/2, there are no ambiguities,
and at a distance exceeding five times the antenna spacing the hyperbolic lines may be
considered as straight bearing lines of position. In operation, the central antenna transmits
continuously at a radio frequency of /s, the outer antennas transmit at a slightly lower radio
frequency /i, and they are sequentially keyed at some fraction, 1/n, of the frequency
difference /2. For a typical POPI station, /i may be equal to 750.000 kc/st /a = 80 cps,
/3 = 750.080 kc/s (obtained by mixing A with /2), and n = 4. With n — 4» the keying
cycle would occur as follows:
First outer antenna on first 1/20 sec
Second outer antenna on second 1/20 sec
Third outer antenna on third 1/20 sec
Space and reference on fourth 1/20 sec
At the receiver, the audio beat frequency /2 = /s — fi (e.g., 80 cps) is applied to a rotating
switch with four contact sectors. In order to control this rotating switch so that the
sequential transmissions will be correctly received, one of the 80-cps outputs from the
rotating switch is used to synchronize an 80-cps oscillator which, in turn, drives a syn-
chronous motor. This motor, through reduction gearing proportional to the factor l/nf
permits 1/20-Bec intervals for receiving the sequential 80-cycle tones corresponding to the
frequency difference of the transmissions from the outer and central antennas of the POPI
station. Since each of the outer antennas has a separate distance or propagation time to
the receiver, there is a correspondingly separate and distinct phase for each 80-cycle tone
sector of the synchronous commutator's output.
It is planned to measure these phase differences as if they were coexistent even though
they actually occur in alternate time sequence. One means proposed for accomplishing
this measurement consists of a separate 80-cycle filter network for each^ synchronous
commutator segment which is capable of ringing or sustaining 80-cycle oscillations after
being energized for about 1/20 sec without exhibiting adverse relative phase shifts between
networks. No report is available at present on results obtained with this critical ringing
network. The present British developments are in an experimental state, although full-
scale trials are contemplated at an early date. It is to be noted that POPI may suffer
the same errors, due to ionosphere phase shifts, that are expected in the Decca system.
TELERAN. (See reference 16.) Teleran, or ieZevision radar and navigation, is a system
that was originally proposed as an aid to air navigation and is discussed in detail in article 6.
22-56 AIDS TO NAVIGATION
It is believed, however, that it has considerable parallel usefulness as a harbor traffic
control type of marine navigational aid, particularly during adverse weather conditions.
Basically Teleran is a television system whereby the central control (shore) station trans-
mits, by television, any essential information to nearby craft. In this manner pertinent
PPI (plan position indication) information, weather warnings, and special instructions
can be instantly presented via the television link to the navigator, using only a standard
television receiver as the shipboard equipment.
FACSIMILE. Because of the increased speed with which navigational information will
be available to the navigator in the future, it is expected that some storing and recording
means will eventually be required in order properly to handle navigational information
that cannot be too well interpreted via oscilloscopes, etc., under busy harbor and related
conditions. Moreover, the need and desire for rapidly printed records of weather, warn-
ings, and congested traffic conditions will serve as a powerful stimulus in the eventual
adoption of such an aid. In view of the relative ease with which facsimile signals can be
multiplexed with other transmissions to the craft being navigated, its introduction is not
expected to be long delayed. In some respects, facsimile transmission becomes a desirable
compromise between the systems of telephoto, television, and teletype transmissions.
Details of the principles of facsimile are discussed in Section 19.
SOFAR. Sofar, or sound /ixing and ranging, is a proposed system for air-sea rescue
service and is a possible long-range navigational aid in the field of underwater sound. It
has been discovered that sound originating at certain depths (often 3000 to 4000 ft) will
be refracted downward by the layers of water above the critical depth, owing mainly to
the temperature gradient in the water, and upward by the layers of water below, owing
largely to the hydrostatic pressure gradient, thus confining the sound energy to a hori-
zontal channel. It has been found possible to use this channel for the transmission of a
distress signal (e.g., by detonation of a suitable explosive charge) over a range exceeding
2500 miles. Reception of this signal by several coordinated and widely spaced hydro-
phone receivers allows an accurate position fix of the distressed craft. Special light-weight
and properly armed charges have been designed for airplane and life-raft applications that
are particularly efficient for air-sea rescue purposes. An initial network of four stations,
at Hilo and Kaneoke in the Hawaiian Islands, and at Monterey and Point Arena on the
California coast, principally for air-sea rescue purposes, cover the long air route from San
Francisco to Hawaii.
REDAR. Redar, or red (and infrared) detection and ranging, is a proposed aid to
marine navigation, similar in principle to radar. In redar, it is proposed to use a search-
light and telescope arrangement in the near-infrared band aboard the ship. The general
techniques and procedures employed in radar are expected to be modified as necessary
and applied to redar. For navigational applications, where rapid redar scanning is not
necessary, a simplified infrared optical range finder operating on well-known optical range
finding principles is proposed. At the present state of infrared investigations, ranges of
3 to 5 miles are predicted during average to clear weather and low humidity conditions,
with accuracies comparable to radar accuracies. Because of the nearly equivalent attenu-
ations of infrared radiations as compared to visible light radiations under fog conditions,
infrared systems are not expected to become a general navigation system. If the need for
very short-range target and obstacle detection becomes pronounced, it is possible that
redar may adequately serve this need in a manner superior to that of most standard radar
systems.
MISCELLANEOUS SYSTEMS. Dingley system (see reference 23) is a frequency-
modulation type of radio navigation aid that basically operates on the pr op agat ion-time-
difference principle, wherein the actual time difference is obtained in the form of a fre-
q.uency difference (or audio beat) . This is accomplished by the use of frequency-modula-
tion emissions from two spaced antennas, whereby there is set up in space a stable pattern
of frequency differences having distinct loci of constant frequency difference. Thus the
Dingley loci are hyperbolas of constant frequency difference as compared to the Loran
loci or hyperbolas of constant propagation time difference. In operation, a central antenna
and at least one other outer antenna are energized with frequency-modulation signals.
The signal received along a radial line from either antenna has a space distribution of
frequencies when that antenna is emitting frequency /o at time fa fi at time fr, fa at time fa
etc. At time ti the signal of frequency /o has traveled to 0*1, and signal of frequency /i is
being emitted at antenna A or at do- The partial table shows the overall conditions respon-
sible for the space distribution of frequencies. Since the table is also applied to give similar
space distribution of frequencies for similar emissions from the second antenna, it can be
seen that those points in space which maintain a constant distance difference to the two
antennas will define a hyperbola along which will be found a constant frequency difference.
Hence, a family of frequency-difference hyperbolas exists for the various differential dis-
OPTIMUM TRANSMISSION PARAMETERS 22-57
tances to the two antennas, and their general similarity to Loran hyperbolas of constant
propagation time difference is immediately apparent. If desired, the reference antenna, A,
can be designated as master and any other antennas, B, C, etc., can be designated as slaves.
INSTAN- INSTAN- INSTAN- INSTAN- INSTAN- INSTAN-
TANEOUS TANEOUS TANEOT7S TANEOUS TAJtfEOUS TANBOUS
TIME FREQUENCY FBBQUENCT AT FREQUENCY AT FREQUENCY AT FREQUENCY
AT do di d2 ds AT dn
*o /o
*i /i /o
*a /2 A /o
*3 /3 /2 A
** /» /n-1 /n-2 /n-3
In view of the above, the Dingley system may be considered a simplified type of Loran
system operating on an F-M basis. Because of the wide band factors generally associated
with frequency modulators, it may be expected that the higher carrier frequencies may be
required with their correspondingly reduced range.
Sonic direction finders have long been employed by the military particularly for anti-
aircraft purposes. Similar sonic direction finders have been employed for underwater
applications. In such applications, a pair of spaced sonic pickup devices (e.g., crystals
acting as hydrophones or sound microphones) have their outputs differentially connected
to yield a cosine law of coupling (i.e., similar to a pair of Adcock dipoles) and have their
resultant output fed to a suitable receiver. When used with a system of underwater sound
beacons the combined arrangement is similar to the radiobeacon system described under
Established Navigational Aids, p. 22-36. Beacon stations are under investigation for
automatically taking sonic bearings on a ship and transmitting by radio the range and
direction of the ship with respect to the beacon's position.
Infrared systems have been proposed which are essentially similar to redar with an
optional infrared beacon system on shore to provide a convenient navigational aid. The
infrared systems, as pointed out previously, do not permit navigating during fog conditions
owing to their inability to penetrate the fog without an attenuation almost as great as that
experienced by visible light. Their chief value would appear to be a black light navigating
system operating under blackout conditions and 'during the absence of fog. Such systems
generally operate in the near infrared region (0.3 to 1.5 microns).
Far infrared (heat-ray) systems have been developed to distinguish targets from their
backgrounds by operating on heat or temperature differences. These systems generally
function in the 8- to 15-micron band and usually operate in a manner wherein the heat
rays are detected by bolometers (see reference 24). One type of bolometer successfully
developed by Johns Hopkins University operates as a superconductor at temperatures
near absolute zero. This superconducting device may include scanning arrangements
whereby target resolution, or definition, roughly comparable to radar definition, can be
attained. Because of atmospheric absorption, ranges beyond a few miles are seldom ob-
tained.
Microwave thermal detection has been reported by G. C. Southworth (reference 25)
in an interesting series of measurements of microwave radiations from the sun. This
phenomenon is to be expected since radio waves may be considered as infrared radiation
of very long wavelength, and a hot body would be expected to radiate microwave energy
thermally. Using such techniques, absorption bands of water vapor have been measured.
It is to be further expected that targets casting a shadow by blanking out radiations over
certain areas might be detected by such microwave thermal and similar techniques. Any
radiation source or any radiation field arranged to cause target shadows is potentially a
means for detecting these targets, whether the frequency of these radiations is sonic or
extends to the cosmic-ray region, and whether or not the emitting source is under control
of the local observer.
12. DETERMINATION OF OPTIMUM TRANSMISSION PARAMETERS
FOR SOME LONG-RANGE RADIO NAVIGATION SYSTEMS
- BASIC CONSIDERATIONS. A long-ran-ge transoceanic radio navigation system for
global application must meet three essential requirements, namely, provide: (1) adequate
signal reception with a sufficient number of coastal or island stations for world-wide
coverage; (2) reliable signal reception at useful levels irrespective of weather, time of day,
22-58 AIDS TO NAVIGATION
season, year, direction, and distance of reception; and (3) an economically feasible arrange-
ment avoiding prohibitive installation and operating costs. P. R. Adams and R. I. Colin
(reference 26) have studied these essential requirements and have arrived at the conclusion
that, if the craft should at all times be within range of two ground stations (in order to
obtain a cross fix) , then these stations should have a minimum range of 1500 miles in order
to insure world-wide double coverage. In addition, they have analyzed the relative
suitability of the various transmission parameters for a reliable 1500-mile range of a long-
range, essentially CW, radio navigation system. These analyses cover the optimum choice '
of frequency, band width, power, modulation, and radiation (antenna) efficiency, and
comprehensively consider these transmission parameters with due respect to the following:
(1) Quasi-minimum field strength (defined as the monthly average of signal strength
measured at the worst hour of the day during the worst months of the worst year) that may
be expected at different places, frequencies, direction of transmissions, etc. (2) Quasi-
maximum significant static intensity (defined as the value of static which is rarely exceeded
at any time and place where the useful signal is likely to have its quasi-minimum field
strength) that may be expected at different places on different frequencies, etc. (3) Signal-
to-noise ratio, based on the ratio of quasi-minimum field strength to quasi-maximum
significant static intensity, in order to determine the ratio's minimum probable value, by
giving proper regard to each factor in the ratio in order to avoid their extreme values
when the time and place of their occurrence may never coincide (the time relationship
for example, depends upon factors such as latitude, time of day, and direction of trans-
mission) . (4) Cost of reliability in the choice of a suitable transmitting frequency (aside
from the normal merit factors determining a choice of transmitting frequency based on
average reception conditions) , the degree and frequency of occurrence of f adeouts, adverse
polarization changes, static conditions, and susceptibility to magnetic storms. (5) Corona
factors, since the size of antenna is partly determined by the required antenna capacitance
that will prevent the antenna charging current from developing a peak voltage in excess
of the critical corona voltage; the latter, in turn, is dependent upon the weather as well
as the dimensional and electrical factors.
As a result of the above types of detailed investigation, employing compiled data and
consideration of the pertinent factors including signal and static strength and fluctuations,
and antenna efficiency, the conclusion is reached that, in an essentially CW type of trans-
mitting system for navigational purposes up to a maximum distance of 1500 miles, ade-
quate reception can be assured with least power input at a transmission frequency of
70 kc/s. These investigations show that the reduction in time lost through fading and
f adeouts offsets the disadvantage of low-frequency transmission and its associated lower
radiation efficiency and higher static intensity. Estimates of power requirements for
several locations and antenna dimensions for handling such power without corona are also
discussed in the above reference.
MODULATION AND BAND WIDTH. The above study makes little mention of
the various methods of modulation by which intelligence may be transmitted at the chosen
carrier frequency. Three paramount points must be considered: (1) the rate of trans-
mission of intelligence on any one frequency is directly proportional to the band width
used; (2) for a normal uniform energy distribution of noise over the frequency spectrum,
the amount of noise energy received is directly proportional to the receiver band width;
and (3) it has been operationally observed that present high-speed craft (including aircraft)
can satisfactorily utilize navigational information furnished at a low rate of intelligence
reception (e.g., 20-cycle modulation) by utilizing integration and average indication sys-
tems. Specifically, amplitude modulation may vary from CW through audio modulation
to pulse modulation transmission. CW transmission provides no intelligence information
except the direction of propagation of the wave; the latter information is extracted by
the receiving station and is not a function of the type of modulation. The receiver band
width required is extremely narrow, thereby reducing band-width noise to the minimum.
Receiver-introduced modulation methods, as described on p. 22-42, may be used to dis-
criminate further against noise and effectively increase the signal-to-noise ratio without
affecting the receiver noise (which is determined by the input circuits). Large bearing
errors may be experienced in pure CW systems at long range, where sky-wave transmission
must be used. These bearing errors cannot be detected easily but may be reduced in
certain cases by means of the receiver modulation methods mentioned. CW transmissions
may be identified by their frequency or by means of very slow keying or on-off schedules
which theoretically require a definite band width but can be reduced to a few cycles, effec-
tively approaching zero.
AUDIO MODULATION can be taken to include modulation frequencies from a few
cycles to several thousand cycles and does not impose prohibitive requirements on trans-
mitter or receiver design. However, in view of the fact that the rate of intelligence trans-
OPTIMUM TRANSMISSION PARAMETERS 22-59
mission need not be high for most navigating systems, it would seem preferable to use
band widths of the order of 10 to 100 cycles and utilize suitable receiving methods in order
to reduce receiver band-width noise to the minimum. It has been operationaUy observed
that modulated radio signals have a higher stability and accuracy performance beyond the
ground-wave propagation range than do CW radio signals. This is apparently due to the
operator's ability to distinguish single-path transmission from multiple-path transmission
(either^ by aural or visual methods) when modulated signals are employed. With CW
radio signals poorer performance results because it is practically impossible to distinguish
the more stable single-path ray from the multiple-path rays with their larger instabilities
and errors. Improved signal-to-noise ratios on desired signals can also be effected in audio
modulated transmitting systems by employing receiver synchronizing procedures to match
the transmitted modulation rate, thereby integrating or averaging out random noise.
Furthermore, improvements in signal-to-noise ratios (e.g., bearing resolution and accuracy
performance) can also be obtained in audio modulated systems by employing the same
receiver-introduced-modulations technique discussed under CW systems and described
on p. 22-42 under direction finders. Modulated systems also permit convenient means for
positively effecting station identification either by keying, time scheduling, or variations
of the modulation rates. It is important to note that modulation rates lend themselves
to accurate synchronization between transmitters and receivers, not only for improving
the signal-to-noise ratio but also for providing a highly effective means for efficiently
employing the frequency spectrum. The spectrum can be conserved by permitting a
number of stations to operate on a common carrier frequency with different known and
stabilized modulation rates, allowing the receiver to select the desired station by syn-
chronizing on the proper modulation. This procedure is already in use in various adapta-
tions as in the Loran method of synchronized pulse modulation, where as many as 16
separate stations in a given area may share the common carrier frequency and are dis-
tinguishable at the receiver by the different synchronous repetition (i.e., modulation) rates.
Pulse modulation systems require a greater band width, and, consequently, the inherent
receiver noise is greater. However, methods of synchronous pulse gating are being de-
veloped which effectively reduce the noise and provide a higher sensitivity to pulse detec-
tion. The wide band required by one transmitter employing pulse modulation can be
offset as in audio modulation by utilizing a number of precisely controlled repetition rates
at the same carrier frequency (as mentioned above in the case of Loran), and by providing
for differentiation between these various rates at the receiver. The greatest single advan-
tage of pulse modulation is the very precise and highly convenient technique available for
time synchronization, which permits effective time differentiation between the various
transmission paths of the arriving wave. The improved signal-to-noise ratio advantage
offered by modulation and pulse synchronization techniques constitutes another great
advantage. However, pulsed techniques become more difficult to apply as the frequency
decreases.
The efficiency of pulse synchronization techniques has been operationally proved in
several instances, such as (1) in the India Theater during World War II where Loran
operation was continuously maintained during the monsoon weather, when all communica-
tion links were erratic or inoperative; and (2) under conditions of severe precipitation
static in Greenland when, again, Loran provided the only operative navigation link,
whereas all communication circuits became unintelligible. The advantages of pulse
techniques for maintaining continuous and reliable service must, therefore, be thoroughly
investigated and included in any comprehensive analysis of the final choice of the operating
parameters for a long-range world-wide navigation system.
Other modulations in addition to the various types of amplitude modulation exist, such
as frequency modulation, phase modulation, and pulse-time modulation. Although no
extensive study has been made of these for long-range navigational purposes it is well
known that frequency and phase modulation possess considerable noise-reducing properties
in addition to the modulation synchronization techniques previously described for improv-
ing signal-to-noise ratios. However, these advantages are partly offset by their usual
wide-band transmission requirements and their general limitation to the higher frequencies
(in order to achieve adequate depth of modulation) where line-of-sight range restrictions
prevail. Pulse-time modulation (PTM) offers the advantage of increased intelligence on a
pulse channel but decreases the number of simultaneous channels allowable at one fre-
quency. It also makes the separation of single and multiple path transmissions more dif-
ficult and prevents use of the precise synchronization techniques necessary for effective
improvements in signal-to-noise ratios. Lastly, hybrid or combination types of modula-
tion and second and third derivative frequency modulation may play increasingly impor-
tant roles as investigation continues into the techniques of such systems.
22-60 AIDS TO NAVIGATION
BIBLIOGRAPHY
1. Comdr. Benjamin Dutton, Navigational Nautical Astronomy. TJ. S. Naval Institute (1942).
2. Aids to Marine Navigation. TJ. S. Coast Guard (1940).
3. Marine Radiobeacons, Engineering Instructions, Chapter 41. U. S. Coast Guard (1944).
4. R. Keen, Wireless Direction Finding. Iliffe & Sons, London (1938).
5. M. K Goldstein, Naval Research Laboratory, R-1896 (HF/DF aboard the U.S.S. CORRY-DD463);
R-1938 (Specifications for Minimum DF Site Requirements); R-2229 (Interpolation Charts for
HF/DF Shipboard Calibrations); R-2469 (HF/DF Collector Locations on a PV-1 Navy Patrol
Bomber). Available through the U. S. Department of Commerce, Washington, D. C.
6. M. K. Goldstein, Naval Research Laboratory, Direction Finder patent applications, Serial Nos.
593,900 (Filed: 5/15/45, Navy Case 5280) and 443,899 (Filed: 5/5/42, Navy Case 3176); and
Patent 2,405,203 issued 8/6/46.
7. Fundamentals of Radar, Wireless World, October 1945, pp. 299-302; November 1945, pp. 326-329;
December 1945, pp. 363-365; January 1946, pp. 23-26; February 1946, pp. 55-56.
8. E. G. Schneider, Radar, Proc. I.R.E., Vol. 34, No. 8, 528-578 (August 1946).
9. John H. DeWitt, Jr., Technical and Tactical Features of Radar, J. Franklin Inst., February 1946,
pp. 97-123.
10. Principles of Radar. M. I. T. Radar School (1944).
11. Electronic Navigation Aids. U. S. Coast Guard, Public Information Division (April 1946).
12. Minimum Specification Brief Nos. 1, #, and 3 Submitted as a Guide for Voluntary Use by Parties
Interested in Navigational Radar. U. S. Coast Guard (Nov. 14, 1945, revised Aug. 1, 1946).
13. J. A. Pierce, An Introduction to Loran, Proc. I.R.E., Vol. 34, 216-234 (May 1946).
14. The Loran System, Electronics, Vol. 18 (November 1945) ; Vol. 18 (December 1945) ; Vol. 19 (March
1946).
15. John E. Clegg, Consol, Beacon Direction Finding Systems of High Accuracy, Wireless Worldt
July 1946, pp. 233-235.
16. Report of Electronic Subdivision Advisory Group on Air Navigation, Bulletin 200, ATSC Eng.
Div. (February 1946). Available through TJ. S. Army Air Forces, Wright Field, Dayton, Ohio.
17. A. Seeley, Shoran Precision Radar, Electrical Engineering (Transactions), April 1946, pp. 232-240.
18. M. K. Goldstein, Proximity Effect of Metallic Fences on Direction Finders, Naval Research Lab-
oratory Report R-1890.
19. Spinning Loop Type Direction Finders proposed by M. K. Goldstein, 1942, see Naval Research
Laboratory Report R-284?.
20. M. K. Goldstein, Facility and Installation Requirements for DAJ/DF Coastal Networks, Naval
Research Laboratory Report R-8079.
21. Early Echo Ranging Sonar, Electronics, Vol. 19, 274-282 (July 1946); Echo Ranging Sonar, Elec-
tronics, Vol. 19, 88-93 (August 1946).
22. Lt. Comdr. D. H. Macmillian, RNR, Precision Echo Sounding and Surveying. Henry Hughes &
Son, London (1939).
23. E. N. Dingley, Jr., A True Omnidirectional Radio Beacon, Communications, Vol. 20, 5, 6, and 35
(January 1940).
24. Papers on Detection of Infra-Red Radiations Given at Winter Meeting of The Optical Society of
America held March 1946. Abstracted in Journal of the Optical Society of America, Vol. 36,
No. 6 (June 1946).
25. G. C. Southworth, Microwave Radiation from the Sun, J. Franklin Inst., Vol. 239, 285-297 (April
1945).
26. Frequency Power and Modulation for a Long-Range Radio Navigation System, Electrical Commun-
ication, Vol. 23, 144-158 (June 1946).
SECTION 23
MEDICAL APPLICATIONS OF ELECTRICITY
BY
CHARLES WEYL
S. REID WARREN, JR.
ELECTROTHERAPY AND SHOCK THERAPY
AHT. PAGE
1. Apparatus 02
2. Electrotherapy 03
3. Shock Therapy 04
DIATHERMY AND HIGH-FREQUENCY
SURGERY
4. Apparatus 04
5. Diathermy Technique 06
6. High-frequency Surgery 06
THE MEDICAL USES OF ULTRAVIOLET
AND INFRARED RADIATIONS
7. Apparatus 06
8. Therapeutic Use of Ultraviolet Radiation 07
9. Therapeutic Use of Infrared Radiation. . 08
ELECTROCARDIOGRAPHY AND ELECTRO-
ENCEPHALOGRAPHY
10. Apparatus 08
11. Techniques 10
ELECTROACOUSTIC DEVICES
ART. PAGE
12. Aids to the Deaf 11
13. The Stethophone 11
ROENTGEN THERAPY
14. Purpose and General Technical Require-
ments. 12
15. Technique 13
ROENTGENOGRAPHY AND ROENTGEN-
OSCOPY
16. Purpose, General Technical Require-
ments, and Technique. . . , 14
17. Apparatus 15
18. Miscellaneous Devices 16
HIGH-VOLTAGE SHOCK AND X-RAY BURN
19. High-voltage Shock 17
UO. X-ray Burn 18
23-01
MEDICAL APPLICATIONS OF ELECTRICITY
By Charles Weyl and S. Reid Warren, Jr.
During the latter part of the eighteenth century Galvani and Volta discovered that the
muscles of dead frogs' legs could be made to move by contact with metals. The descrip-
tions of their experiments indicated that they were establishing a difference of electric
potential between nerves and/or muscles of the frogs' legs and that this applied difference
of potential caused a motion of the muscles. Since that time, many techniques have been
devised for using electrical apparatus for studying physiological functions, for the diag-
nosis of disease, and for therapeusis. During the twentieth century the development of
these medical applications of electricity has become accelerated and, particularly since
1925, new methods have been developed, tested, and applied to clinical practice. Al-
though some of these techniques have become standardized by accurate experimental in-
vestigations, nevertheless, the biophysical explanations of many of the techniques are al-
most completely unknown. Although frequently the electrical apparatus and the tech-
niques for their use are simple, an accurate knowledge of the results of the technique has
been impeded by differences in individual patients, by lack of knowledge of the physio-
logical factors involved, and by a lack of proper control of the apparatus and technique.
Thus there exists a fertile field for investigation in which physicists and engineers are
aiding physicians in problems of electromedical diagnosis and therapeusis.
With the accelerated development of the electromedical methods which were known
before 1925, and also of the new methods which have been introduced since that time, there
has been a great increase in the literature of the field. Furthermore, the applications of
many of the newer devices and techniques to medicine are subsidiary to their applications
in other scientific fields. This section is organized on the basis of these factors. Each
article contains the following items: (1) a list of the fundamental components of the elec-
trical apparatus required for a particular electromedical technique and an example of their
combination into a practical, useful apparatus; (2) a brief description of the electromedical
technique and examples W its use; (3) a list of references to papers and books in which the
electromedical apparatus and technique are discussed in detail.
The literature of the medical applications of electricity uses terms quite different from
those employed by physicists and engineers, and some of them are extremely confusing.
For example, the term electrotherapy is sometimes used as a generic to represent nearly all
the electromedical techniques except those involving x-rays; it also often represents solely
those techniques described in the next article involving the conduction through parts of
the body of direct, pulsating, and alternating currents.
ELECTROTHERAPY AND SHOCK THERAPY
1. APPARATUS
The apparatus employed for generating direct and alternating currents for electro-
therapy has many forms, all of which are fundamentally of simple design from the engi-
neering point of view. The requirements are as follows: (1) direct current, 0 to 80 volts,
0 to 50 ma, with a continuous resistance control; (2) alternating current at commercial
frequencies from 0 to 50 volts rms, 0 to 25 ma; (3) a method for periodically surging or
modulating the alternating currents mentioned in (2) ; (4) an induction coil operated by
direct current with a mechanical interrupter; (5) a device for providing pulsating current
at frequencies from 10 to 100 pulses per second.
Occasionally an attempt is made to construct an apparatus which will supply all these
wave forms. Usually, however, the physician purchases different pieces of apparatus for
each purpose. At present, the trend is toward the construction of apparatus which
operates from an a-c source of 110 volts, 60 cycles. For example, the d-c generator may
take the form of a small 1 : 1 ratio transformer with the secondary connected to a full-wave
rectifier and filter system. Across the filter system is connected a potentiometer, and the
electrodes are connected to two terminals of the potentiometer. The surging devices are
generally motor-driven variable resistances. The apparatus used for these purposes has
not been standardized and therefore it is not possible to give typical wiring diagrams.
23-02
ELECTROTHERAPY 23-03
The arrangements for protection of the patient from excessive electric shock are, in many
installations, inadequate.
A number of accessory parts comprising, for example, specially designed electrodes and
a timer for controlling the length of treatment are required.
The development of technique in electrotherapy is based entirely on empirical results
frequently acquired from doubtful interpretations of meager data. Since remarkably
little attention has been paid to the precise measurement of voltage and current, many of
the accumulated data are of doubtful value.
^ Treatments usually have a duration of 1 to 15 xnin. In general the physician specifies
his technique by a measurement of the current which flows through the patient, and the
duration of the treatment.
2. ELECTROTHERAPY
It has been known for many years that passage of electric currents through the human
body may cause important physical and physiochemical changes within the tissue. The
following results form the basis of methods of diagnosis and treatment by the passage of
electrical currents through the body: (1) the transfer of ions from outside the body into
the treated part; (2) the transfer of ions from within the body to an electrode outside; (3)
the production of heat within the living tissue; (4) the stimulation of nerve and muscle
fibers.
To accomplish these purposes, direct currents, pulsating currents, and alternating cur-
rents are used. The following paragraphs describe the applications of each of these sev-
eral forms of current.
ELECTROCHEMICAL CAUTERIZATION. A flow of direct current (called galvanic
current in electrotherapy) through the body generally serves its therapeutic purpose by
destroying diseased tissue. If platinum electrodes are applied to a diseased part which is
near the surface of the body, and a direct current is made to flow between the electrodes,
an acid tends to form by electrolytic action at the anode, and an alkali at the cathode.
The destructive action of such chemicals is well known, and frequently it is possible to
control the destruction of tissue by means of the electrical method for the production of
these chemicals. Such a procedure is called electrochemical cauterization. Usually only-
one metallic electrode is placed in contact with the tissue. The other electrode, called the
indifferent electrode, consists of a metal disk several inches in diameter held against a pad
of cotton soaked in a solution of sodium chloride and placed against the skin of the pa-
tient. The transfer of ions from the salt solution apparently has negligible effect on the
human body. Electrochemical cauterization is used for removing superfluous hair, warts,
and small rodent ulcers, and also in the treatment of certain skin diseases.
IONTOPHORESIS. If one hand of the patient is placed hi a liquid electrolyte, and this
electrolyte is used as an electrode, it is possible by the application of direct current to>
transfer ions from the solution into the body. This process is called iontophoresis. The
physiological results of treatment by this method have not been adequately explained.
Some work has been done for the purpose of effecting local anesthesia by the transfer of
ions from cocaine into the body at chosen places. Metallic ions have been introduced,
and it is claimed that the recombinations that occur within the body provide small quan-
tities of atomic metal or of metallic salts at the site of disease. Other chemicals such as
acetylbetamethylcholine chloride and histamine have been used for the treatment of
specific disorders.
CATAPHORESIS. If a semi-solid electrolytic gelatin is formed in the shape of a
cylinder and two metal plates are placed at the ends of the cylinder, a direct current may
be made to flow through the gelatin. After a few minutes have elapsed, there is an in-
crease of water at the cathode and a decrease of water at the anode. This phenomenon is
apparently caused by changes in osmotic pressure due in turn to the current flow. This
procedure is sometimes used to remove undesired liquids from skin lesions. It is called
cataphoresis.
MISCELLANEOUS. It has been found that muscles which are in a state of fatigue
become considerably strengthened after treatment with direct current. It has also been
claimed by many workers that the passage of current causes exhilaration of some patients,
and, on the other hand, with a slightly different technical procedure, the same type of
treatment may produce drowsiness. The causes of these effects are unknown.
The passage of small direct currents through the body causes no pain. However, a
sudden change in the amplitude of the current produces muscular twitching and pain.
Normally, d-c treatments require a source capable of adjustment from 0 to SO volts. The
current passing through the body may be from 1/2 to 50 ma. Because of the muscular
twitching described above, it is particularly important that the current be adjusted slowly
23-04 MEDICAL APPLICATIONS OF ELECTRICITY
to the desired value. Quantitatively, it is usual to increase the current linearly with time
at the rate of 1 ma per min. The d-c resistance of the two arms and the trunk of the
average adult is approximately 1400 ohms. This resistance is measured by suspending
the hands in salt solutions, thereby overcoming the high resistance of dry skins.
The passage of alternating current of frequency less than a few thousand cycles per
second involves a sensation of pain and twitching of the muscles. The intensity of mus-
cular reaction and pain increases with the amplitude of the current and with the frequency
up to an indefinite limiting value of several thousand cycles per second. When the fre-
quency is raised above this value, the sensation decreases and finally disappears unless the
amplitude of the current is sufficient to produce appreciable heat.
The steady application of alternating currents of a few milliamperes of commercial
frequencies is extremely painful and dangerous. Therefore a device is required to produce
a surging sinusoidal current which may be described in the following manner. At the
beginning of the treatment the alternating current is zero amplitude. Over a period of
the order of 2 sec it is increased to a maximum and decreased to zero. There follows a
rest period of about 2 sec, and then the surge is repeated. Apparently the application of
60-cycle alternating currents causes contraction and extension of the muscles. Treat-
ment by this method has been recommended for paralyzed muscles or muscles damaged by
disease.
FARADIC AND MISCELLANEOUS WAVE FORMS. Various other types of alter-
nating and pulsating currents have been recommended for therapeutic use. It will suffice
to list a few of these: (1) the secondary current from an induction coil, called faradic cur-
rent in electrotherapy; (2) currents produced by the periodic charge and discharge of con-
densers; (3) pulsating current of various wave forms produced by mechanical interrupters;
(4) high-frequency brush discharge by means of a Tesla coil. Standardization of such
methods will require a careful oscillographic analysis of the electrical parameters combined
with a statistical analysis of the clinical results.
3. SHOCK THERAPY
In certain mental disorders it has been found that if a convulsive shock is produced in
the patient by means of drugs, or by electric currents passing through the brain, improve-
ment in the condition of the patient is often observed. The techniques of shock therapy
are still based chiefly on empirical data. It is to be noted that the threshold at which
electric shock of the brain will cause convulsion is relatively close to the higher lethal
threshold. It is, therefore, necessary to control the shock precisely. Shock treatments
are usually given in a series of from six to twelve treatments during periods of a few weeks.
It is found that, using electrodes placed approximately over the two temples, currents
of the order of 1 amp, adequate to produce convulsion, are caused to now by a 60-cycle
alternating voltage of approximately 100 volts. Thus, the apparatus for shock therapy
consists essentially of a transformer, the output of which can be continuously varied, and
a timer capable of producing exposures from 0.1 sec to 0.6 sec in steps of 0.1 sec. Motor-
driven timers, time-delay relays, and electronic timers have been used to produce the de-
sired intervals of shock. In order to avoid fatal accidents, it is important in these devices
to use circuits such that the failure of a component will result in a great decrease in the
output voltage.
BIBLIOGRAPHY
Cumberbatch, E. P., Essentials of Medical Electricity. Mosby (1929).
Glasser, Otto, Editor, Medical Physics. Year Book Publications, Inc., Chicago, IU. (1944). Physical
therapy, low-frequency currents, pp. 1068-1073.
Kovacs, Richard, M. D., Electro-therapy and the Elements of Light Therapy. Lea and Febiger (1932).
Osbourne, S. L., and H. J. Holmquest, Technic of Electro-therapy and Its Physical and Physiological
Bases. Charles C. Thomas, Springfield, IU. (1944).
Electric Convulsion Therapy in Mental Disorders, Psychiatric Quart., Vol. 14, 719 (1940).
DIATHERMY AND HIGH-FREQUENCY SURGERY
4. APPARATUS
Generators of high-frequency alternating current, from 750 kc per sec to 3000 Me per
sec, have been used to raise the temperature of parts of the human body in the techniques
known as diathermy and high-frequency surgery.
DIATHERMY AND HIGH-FREQUENCY SURGERY 23-05
There are two general types of diathermy apparatus. In the first type, a high-voltage
transformer is connected to an oscillatory discharge circuit consisting of a spark gap, con-
densers, and an inductance. Loosely coupled to this oscillatory circuit is a secondary
circuit to which the patient is connected. A high-frequency ammeter is connected in
series with the patient to measure the magnitude of the treatment current. Figure 1 is a
diagram of such a generator. More recently vacuum-tube oscillators (see Section 7) have
CD II®
FIG. 1. Diathermy Apparatus Using Spark-gap High-frequency Generator
1, Step-up transformer; 2, spark gaps; 3, condenser, and£4/ inductance forming oscillatory circuit
which resonates at 500-1000 kc; 5, coil coupled to oscillatory circuit; 6, 7, condensers; 8, high-
frequency a-c ammeter; 9, leads to electrodes.
been designed for this purpose. They are connected in a manner similar to that shown in
Fig. 2. It will be noted that the two circuits are identical in all essential features with the
two types of radio transmitters known respectively as spark and continuous-wave trans-
mitters.
Various techniques are used for producing a high-frequency electromagnetic field within
the part that is to be treated. Thus, the output of the oscillator is sometimes applied to
two metallic plates between which the part of the body to be treated is placed. Alter-
natively the output of the oscillator may be fed to a cable which can be wrapped in the
FIG. 2. Diathermy Apparatus Using Vacuum-tube Oscillator
1, 110-volt, 60-cycle a-c supply; 2, plate voltage transformer; 3, vacuum tube; 4, 5, oscillating cir-
cuit; 6, grid leak and grid condenser; 7, blocking condenser; 8, r-f choke; 9, inductively coupled output
coil; 10, output leads to ammeter and patient. The cathodes of the! vacuum tubes are heated by cur-
rent from an additional secondary coil (not shown) of transformer 2.
form of a solenoid around a body part or shaped into a spiral coil (the technical term^is
pancake) which can then be fixed against one side of the part to be treated. The special
electrodes required for surgery are described in article 6.
Apparatus using a magnetron operating at 2450 Me is now available. Radiation ia
emitted by one of several parabolic reflectors 6 to 10 cm in diameter excited by a dipole.
The radiation is thus confined to a relatively sharp beam.
Because of the very important danger of interference with communication facilities,
the F.C.C. has prescribed the frequencies permitted for diathermy and the frequency
23-06 MEDICAL APPLICATIONS OF ELECTRICITY
stability that is required. The frequencies so assigned are: 13,560 kc =fc 6.78 kc;
27,120 kc± 160.00 kc; 40,680 kc ± 20.00 kc; 2450 Me ± 50 Me, available for experi-
mental work.
5. DIATHERMY TECHNIQUE
If the frequency of the alternating current applied to the human body is indefinitely in-
creased, an ill-defined point can be found (order of magnitude of 10,000 cycles per second)
beyond which no sensation other than warmth is felt. The minimum amplitude of alter-
nating current which produces pain by passage through the human body varies with the
frequency of the alternating current and with the subject. Average values obtained by
a number of workers are as follows:
AVERAGE
FREQUENCY, TOLERANCE,
cycles per second milliamperes
60 3- 8
10,000 tolerance current, increasing gradually to 25- 30
100,000 tolerance current, increasing quickly to 250-600
Heating effects, only, are noted above 100,000 cycles per second. As a result it is pos-
sible to increase the current flowing through the body to values as high as 5 amp. This
causes a sensible dissipation of heat within the tissue. For this purpose frequencies
-above 750 kc per sec are used. It has been discovered that heat produced internally
is effectual in the treatment of certain diseases. The name diathermy has been given
to the treatments characterized by the internal heating effect of high-frequency alter-
nating currents. Electrodes several square centimeters in area are used in order that
the current may be distributed approximately uniformly over a large area. Other ma-
chines in which the patient is not in contact with electrodes, but is placed in a strong high-
frequency electromagnetic field (between "condenser" electrodes), have been constructed
for the purpose of heating the entire body or, more commonly, large portions of the body.
It is possible to raise the body temperature as much as 3 or 4 deg C by this means. The
method has proved useful in the treatment of syphilis, pleurisy, neuritis, and other diseases.
The currents normally used range from 0.5 to 5.0 amp.
6. HIGH-FREQUENCY SURGERY
If one large electrode is applied to a part of the body and a second electrode consisting
of a large platinum needle is brought in contact with any other part of the body, the re-
sultant current density is so high at the point of application of the needle that the tissue
may be completely destroyed by heat. This method, which is called electrosurgery, is a
relatively recent development. The small blood vessels severed by means of the high-
frequency knife are normally sealed by the heating action, and bleeding is therefore con-
siderably reduced. Basically, there is no difference between the equipment used for
diathermy and for high-frequency surgery.
BIBLIOGRAPHY
Cumber-batch, E. P., Diathermy. London (1929).
Kova^s, Richard, M. DM Electro-Therapy and Light Therapy, Lea and Febiger (1932).
Osbourne, S. L., and H. J. Holmquest, Technic of Electro-Therapy, and Its Physical and Physiological
Bases. Charles C. Thomas, Springfield, 111., pp. 315-744 (1944).
THE MEDICAL USES OF ULTRAVIOLET
AND INFRARED RADIATIONS
7. APPARATUS
Apparatus for the production of ultraviolet radiation includes the carbon-arc generator,
the quartz-enclosed mercury-arc generator, and the mercury glow-discharge lamp enclosed
in quartz or Corex, a glass which transmits a useful amount of ultraviolet radiation. One
jof the chief objections to the carbon-arc generator is its production of relatively high-
intensity visible and infrared radiations. In addition to the above-mentioned lamps,
.which have relatively high outputs, several special lamps have been developed for home
iase under medical supervision.
THERAPEUTIC USE OF ULTRAVIOLET RADIATION 23-07
One of these — the Mazda US lamp — is rated at 110 volts 275 watts. At a distance of
24 in. this lamp will produce a mild reddening (erythema) of the skin in about 5 min. The
lamp is strong in those radiations that produce sunburn (2800 to 3200 angstrom units).
There is also a relatively strong infrared beam produced chiefly by a tungsten filament in
an atmosphere of argon and nitrogen.
The outer envelope of the Mazda RS lamp is made of special glass that transmits in-
frared and visible radiation, and ultraviolet radiation of wavelengths greater than 2800 A.
A reflecting surface is deposited on the interior surface of this envelope; the radiation is
emitted through the circular (12-cm diameter) end of the lamp opposite the screwplug.
A tungsten filament, which operates as a series ballast after the initial preheating period,
is mounted in the outer envelope; the space is filled with argon and nitrogen.
Within the larger outer envelope, there is a quartz capsule containing an oxide-coated
filament and a second, initially cold, electrode; this capsule contains mercury.
When the lamp is initially connected to 110-volt 60-cycle alternating current, the outer
(tungsten) filament and the inner (oxide-coated) filament are connected in series. After
approximately 30 sec, when the oxide-coated filament acquires a sufficiently high tem-
perature for copious emission of electrons, a thermal delay switch within the tube operates
to connect the initially cold electrode of the quartz capsule to the terminal of the supply
opposite from the terminal connected, through the tungsten filament, to the oxide-coated
filament and disconnects the oxide-coated filament. The mercury arc then strikes, be-
coming stable as the initially cold electrode becomes heated by bombardment. The arc
in the mercury vapor at a pressure of approximately 1.1 atmospheres then operates in
series with the tungsten filament; the filament and arc emit ultraviolet, visible, and in-
frared radiation. The manufacturer recommends a 1-min. "warm-up" period before use.
Glow-discharge mercury tubes operating at voltages as high as 5000 volts and currents
of the order of 15 ma produce radiation almost entirely of the emission frequency line of
mercury having a wavelength of 2537 A. This radiation is strongly bactericidal. Since
it also requires low-power input, this type of lamp is often used to irradiate the area in
operating rooms and in other places where air-borne bacteria are to be mimmized. Ex-
periments using these devices in schoolrooms are being conducted.
Since the mercury-arc lamp enclosed in quartz produces a relatively high-intensity radi-
ation at wavelengths from 2483 to 4047 A, and since this apparatus is relatively stable
in operation after a few minutes of operation, it is now the most common source for med-
ical purposes. The total power input to such a device is from 250 to 400 watts, and its
output of ultraviolet radiation is of the order of 225 microwatts per square centimeter at a
distance of 1 meter without a reflector.
Special photoelectric cells connected to integrating circuits and counters have been
devised to measure the outputs of ultraviolet generators throughout various bands of
wavelengths. However, such standardizing measurements have not been very often
applied to clinical use.
Infrared radiation is produced chiefly by electrically heated wire operating at temper-
atures from 800 to 1600 deg C or by means of incandescent tungsten lamps with or without
filters.
8. THERAPEUTIC USE OF ULTRAVIOLET RADIATION
It has been known for many years that sunlight has a definitely beneficial effect upon the
human body. {Since 1800 the spectra of light emitted by the sun and by electric arcs have
been analyzed and more attention has been directed to the specific photochemical effects
of the various parts of the spectrum. More or less arbitrarily, ultraviolet radiation has
been defined as radiation with a range of wavelengths from approximately 4000 to about
40 A (1 angstrom unit = 10~8 crn). The solar spectrum extends down to approximately
2900 A but under average atmospheric conditions at sea level there is negligible radiation
below 3000 A. It has been shown that most of the ultraviolet radiation incident upon the
human body from the sun or from artificial sources is absorbed in the surface tissues. The
penetration is 0.1 mm or less.
There has been much speculation as to the biological processes produced by ultraviolet
radiation, which has so far resulted largely in contradictions and disagreements among
authorities on the subject.
The first noticeable effects of ultraviolet radiation are erythema, or reddening of the
skin, usually followed by pigmentation. Each individual has a different tolerance to
ultraviolet radiation. What may cause a pronounced erythema in one may produce no
effect upon another. It has been discovered that certain non-soluble fatsr particularly
ergosterol, form vitamin D when irradiated by ultraviolet rays. This substance is present
in the human body, and normal exposure to sunlight is one method for supplying the
23-08 MEDICAL APPLICATIONS OF ELECTRICITY
definite need of the body for vitamin D. Although there is no question as to the beneficial
effects of sunlight and artificial sources of ultraviolet radiation when exposures are care-
fully controlled, enthusiasm on the part both of physicians and of laymen has led to dan-
gerous overexposures to both natural and artificial sources of this form of energy. It has
not been proved that exposure to direct sunlight is essential to the physical well-being of
the normal healthy human.
Treatment by ultraviolet radiation is useful in cases of rickets, high blood pressure, and
some skin diseases. It has been shown definitely that ultraviolet radiation produces
directly and indirectly a substantial rise in the amount of calcium and phosphorus in the
blood. The treatment is in general use for rickets in infants and has been remarkably
successful. Certain experimenters believe that the effect of ultraviolet rays on the nervous
system is stimulating. A number of psychiatrists have recommended the treatment for
neurasthenia and some of the psychoses.
£ After Pasteur's discovery that small living organisms are the cause of many diseases
and also of fermentation, experiments were performed to find the effects of various types
of radiation upon these organisms. It was found that ultraviolet rays were potent in
bactericidal action, particularly in the 2600 A region.
Different parts of the body vary considerably in sensitivity. For example, twenty to
thirty times as much ultraviolet radiation is required to produce an erythema of the soles
of the feet than of the face, which is the most sensitive part. Even small doses which
penetrate to the eyeball can cause serious damage; therefore all patients receiving ultra-
violet treatment are required to wear goggles made of glass which absorbs practically all
the ultraviolet radiation. Practically no ultraviolet radiation is transmitted through
window glass and very little through smoky atmosphere. Therefore sunlight may be used
as a source of therapeutic ultraviolet rays to the best advantage in special regions — for
example, in high mountains where there are generally very few clouds and practically no
dust or smoke. Since the ultraviolet content of sunlight varies with latitude, season, time
of day, and atmospheric conditions (such as ozone, water vapor, dust, and smoke) it is im-
portant to measure the intensity in the region of 2900-3200 A during treatment.
9. THERAPEUTIC USE OF INFRARED RADIATION
Infrared radiation is used for surface heating, either of a small circumscribed area or for
the surface of an entire leg or arm. One of the chief effects is the production of increased
blood flow near the surface, and this may, in turn, cause more deep-seated changes.
It is possible also to change the temperature of the entire body. Thus the body may
be placed in a heat-insulated housing inside of which incandescent lamps or other heating
elements raise the temperature of the body and of the area surrounding it. Since there is
no way for this heat to be entirely radiated, the temperature of the body is caused to rise.
Such whole-body heating may also be accomplished by means of diathermy.
BIBLIOGRAPHY
Bernhard, O., Light Treatment in Surgery. Arnold, London (1923).
Duggar, B. A., Biological Effects of Radiation, Vol. 1. McGraw-Hill (1936).
Finsen, N. R., Phototherapy. Arnold, London (1901).
Glasser, Otto, Editor, Medical Physics. Year Book Publications, Inc., Chicago, 111. (1944). Physical
therapy — heat and cold, pp. 1043-1054; light, pp. 1054-1068; radiation, sources of ultraviolet and
infrared, pp. 1157-1163.
Laurens, Henry, The Physiological Effects of Radiant Energy. Chemical Catalog Co. (1923).
Bollier, A., Heliotherapy. Frowde, Hodder and Stoughton, London (1923).
Osbourne, S. L., and H. J. Holmquest, Technic of Electro-therapy and Its Physical and Physiological
Bases. Charles C. Thomas, Springfield, 111. (1944). Ultraviolet radiation, pp. 235-313; infrared
radiation, pp. 194-234.
ELECTROCARDIOGRAPHY AND ELECTRO-
ENCEPHALOGRAPHY
10. APPARATUS
Muscular contractions and the functioning of nerves are accompanied by measurable
differences of electric potential at the surface of the body. Thus the time-varying dif-
ferences of potential between the right arm and the left arm, the right arm and the left leg,
ELECTROCARJDIOGKAPHY
23-09
the left arm and the left leg are used by cardiologists to interpret the action of the heart;
these differences of potential are called respectively the potentials of Lead I, Lead II, and
Lead III. The measured differences of potential are of the order of a few millivolts. An
electrocardiogram for Lead II for a normal patient and a heart sound record made simul-
taneously are shown in Fig. 1. For the electrocardiogram, a vertical deflection of one
small division corresponds to a difference of potential of 0.2 mv.
I®
fa i- ~^~
V /?N
V I
© ®
J
© © i
FIG. 1. Electrocardiogram
Lower. — Electrocardiogram, Lead II, normal patient. The letters P, Q, R, S, and T are standard
symbols for designating the waves thus marked.
Upper. — Heart sound record made simultaneously with the electrocardiogram above.
Electrocardiographic apparatus requires the following component parts: (1) a device
for transforming the electromotive force generated by the heart into the motion of a light
beam or of a shadow; (2) a camera with moving film or paper to record the deflections of
the light beam or shadow; (3) devices for calibrating the abscissa (time) and the ordinate
(electromotive force) on the electrocardiogram.
Einthoven developed a system similar to that shown in Fig. 2. A silvered quartz string
with variable tension is held perpendicular to an intense constant magnetic field produced
by an electromagnet. A calibrated ex-
ternal source of electromotive force is
used as standardizes A variable resist-
ance and associated battery are used to
compensate for skin currents (described
below under technique). A specially
adapted camera, with a tuning fork or
other timing device, is used to record
the deflection of the string produced by
the heart action.
It has been shown that the Einthoven
string galvanometer produces distortion
due to the change in its response with
frequency; furthermore, as is described
below, it requires, for an adjustment of
sensitivity, a change in the string ten- 2 Outline Diagram of Einthoven String Electro-
sion which produces further distortion. cardiograph
Therefore, efforts were made to use lf galvanometer conducting string of silvered quartz,
galvanometers with more uniform fre- suspended with controllable tension between the poles
quency response. It was found that of an electromagnet (not shown) which produces .a mag-
j, , AH . , j ,T_ netic field in the direction of the arrow 2; 3, light source
the use of carefully constructed ther- to Obtam, with system of lenses not shown, an image of
mionic amplifiers in association with the string upon the moving photographic film in the
these new galvanometers provided in- ^^'i^^^^M* S£S±£S!
struments of great flexibility ana sta- a series circuit which introduces an adjustable electro-
bility. The cardiographic p'aper or film motive force in series^ with the string to compensate for
can be driven by a synchronous motor,
so that the time abscissas are the same
for all cardiograms.
leads to the patient.
It is most convenient to describe the technique of electro car diography by referenee^to
the Einthoven instrument shown in Fig. 2. A resistance 5 is connected in parallel with
the string, reducing its sensitivity by a ratio of 10 to 1. One area on each arm of the
patient is rubbed with a contact paste and a metal electrode is applied. This corresponds
to the designation described above as Lead I. A switch is closed connecting the patient
to the electrocardiograph. The galvanometer deflects, owing to what is called skin cur-
rent. The slide of 9 is then moved until the galvanometer string is returned to its zero
position. This operation balances out the skin current, which is constant and plays no
part in the interpretation of the electrocardiogram. After the compensator is adjusted,
23-10
MEDICAL APPLICATIONS OF ELECTRICITY
the shunt 5 across the galvanometer string is disconnected. This increases the amplitude
of swing of the fiber. The standardizing circuit is then connected by closing switch 14
and opening switch 11. The circuit 12, 13, 15 is designed to produce a potential drop of
1 mv across the resistance 13. This throws the image of the string across the screen. An
adjustment of the mechanical tension of the string is made so that the application of the
1-mv standardizing voltage produces a deflection of exactly 1 cm. The standardizing
voltage is then removed by opening switch 14 and closing switch 11, and the electro-
cardiogram for Lead I is taken by means of a paper moving at constant speed past the
beam of light through the galvanometer. For each centimeter deflection of this record
an electrocardiographic impulse of 1 mv is necessary. The same procedure is followed for
Leads II and III, The moving photographic paper passes before a glass screen upon
which lines 1 mm apart are ruled in the direction of motion of the paper, while a
synchronous motor turns a bladed wheel through the light beam at right angles to the
direction of motion of the paper, producing a series of time-marking lines spaced at
0.04-sec intervals.
The procedure described can be accomplished quickly in practice. The entire operation
is illustrated in Fig. 3. This description applies to the older type of electrocardiograph,
from which the underlying principles can be clearly
understood. The routine use of a modern electro-
cardiograph is characterized by practical simplic-
ity, although a description of this procedure would
not illustrate so clearly the fundamental charac-
teristics.
The modern electrocardiograph may be battery
operated or it may operate from a 110-volt 60-cycle
source. It is usually a self-contained portable de-
vice, and the records may be produced on film or
photographic paper or — more recently — may be
directly recorded on paper that may be examined
as soon as it is produced. These devices are
equipped with stabilized audio-frequency ampli-
fiers feeding into specially designed galvanometers.
The frequency characteristic of these electro-
cardiographs results in the reproduction, at nearly
constant levels, of frequencies from 0.5 to 50 or
100 cycles per second. Because of the susceptibility of these high-impedance amplifiers
to hum pickup, special hum-bucking input circuits are incorporated.
An electroencephalograph is used to record time-varying changes of potential between
pairs of electrodes in contact with various parts of the scalp; the magnitudes of these dif-
ferences of potential are from a few microvolts to approximately 100 mv. The component
frequencies of the electroencephalographic signals are less than 1000 cycles per second.
It follows, therefore, that an electroencephalograph can be a device similar to an electro-
cardiograph except that (1) the amplification must be about 100 times greater in the
electroencephalograph, and (2) it is considered essential to provide fourteen-channel in-
put (and two- to six-channel output) for the electroencephalograph instead of four-channel
input which is used in the electrocardiograph.
.!3 lliUClbl OibCU. J.JUL JL' J.g. O. JL.JJL.Li3 U.O»l^J.AjJI
•ill
FIG. 3. Calibration of Electrocardiograph
The calibration record which is made at
the t end of the electrocardiogram of each
patient. At (1) the standardizing voltage
of 1 mv is connected in series with the gal-
vanometer, causing a deflection of 1 cm to
(2). The electrocardiogram is of Lead II,
normal patient.
11. TECHNIQUES
Since the middle of the nineteenth century it has been known that an electromotive
force is generated within the heart during the period of contraction of this muscular organ.
The precise causes of this effect are unknown. Nevertheless, the methods for measuring
the variations of this electromotive force with time have been carefully standardized, and
statistical records have been made for many years. By associating these records with
case histories, a technique has been evolved for diagnosing certain diseases of the heart
which is, in many instances, remarkably valuable. The development of electrocardiog-
raphy has shown the benefits of carefully standardized scientific methods more than most
other special fields of medicine in which electrical equipment has been used.
When the so-called "brain waves" are recorded by means of an electroencephalograph
the wave forms are found to vary with age, with the somatic state of the individual, with
the state of mental health of the individual, and with many other factors. Thus the de-
velopment of this field of investigation has been based upon the recording of many elec-
.trpencephalograms, their analysis and intercomparison, and finally attempts at diagnosis
^ased, > upon these analyses. The electroencephalograph now finds clinical use in the
corroborative diagnosis of epilepsy and, in many cases, in the localization of brain tumors.
THE STETHOPHONE 23-11
BIBLIOGRAPHY
A8fe^' Richard- and Edgar Hull, Essentials of Electrocardiograph, The MacmiUan Co., New York
(.1945;.
Berger, EC., Archives of Psychiatry, Vol. 87, 527 (1929); Vol. 100, 301 (1933).
Glasser, Otto, Editor, Medical Physics. The Year Book Publications, Inc., Chicago, 111. (1944).
Electrocardiography, pp. 352-360; electroencephalography, pp. 361-371.
Jasper, H. H., and L. Carmichael, Science, Vol. 81 (January 1935).
Lilcotf, W J3 M. B. Rappapart, and S. A. Levine, Continuous Recording Electrocardiography, Am.
Heart /., Vol. 28, 98-114 (July 1944).
Traugott, Paul, Electroencephalograph Design, Electronics, Vol. 16, 132-144 (August 1943).
ELECTROACOUSTIC DEVICES
12. AIDS TO THE DEAF
Those whose hearing is deficient require aids designed upon the basis of a quantitative
study of their relative deafness. For this study a device called the audiometer is used;
this instrument consists essentially of a vacuum-tube oscillator capable of producing
practically pure tones accurately controllable as to pitch and intensity in head receivers.
The pitch proceeds by octaves from 32 double vibrations per second to 16,384, with an
intensity^range of 109. Charts called audiograms have been made, showing the thresholds
in sensation units, of hearing and of pain, for thousands of subjects with normal hearing.
By comparing the audiograms, both the type and degree of deafness may be estimated.
This constitutes a valuable aid in diagnosis and also is a useful adjunct for the prescription
of hearing aids.
Many who are deaf learn to read lips. Care must be taken, therefore, to eliminate this
source of error from tests of hearing aids, even though lip-reading may become a part of
the method of understanding speech after the hearing aid is adopted. Some who have
beon deaf for a period of years require a considerable amount of time to learn to under-
stand sounds heard with the aid of an electric device.
Hearing aids usually consist of a small microphone, a battery, and a special light-weight
electromagnetic or crystal receiver. The system is designed to produce at the ear, as
nearly as possible, an amplified replica of the sounds incident upon the microphone. If
such a simple device does not amplify sufficiently, an amplifier using vacuum tubes may
be added.
In recent years, the development of so-called "miniature" and "hearing-aid" tubes and
of small batteries and printed circuits has considerably reduced the size and weight of
such equipment.
More elaborate devices have been made for those whose hearing is especially deficient,
in some instances the apparatus being designed to suit the individual requirements as
determined from studies of the audiograms and the personal characteristics of the subject.
Among the more elaborate examples of this type of hearing aid is the two-channel system
in which, two high-fidelity, velocity microphones are connected individually to two high-
quality amplifiers, equipped with filters especially designed to compensate for the auditory
deficiencies of the subject. The outputs of these two systems are then connected to in-
dividual headphones so that each ear of the subject has an entirely separate channel,
separately connected, and affording corrected binaural (two-ear) hearing.
13. THE STETHOPHONE
About 1924 a device for picking up human heart sounds by means of a microphone and
amplifying these sounds was developed and given the name "stethophone." The original
purpose of the device was to make it possible for students in the amphitheater of the heart
clinic to listen simultaneously with the demonstrator to the heart sounds of the patient
under examination. The device had the additional advantage over the ordinary stetho-
scope of producing louder sounds in the listener's ear. It was further shown that by the
insertion of electrical filters it was possible to eliminate portions of the audible frequency
spectrum in order to concentrate upon certain specific sounds. This means of selective
listening proved an aid in the diagnosis of murmers and other cardiac abnormalities.
More recently this device has been used by physicians who are somewhat hard of hearing.
RECORDING OF HEART SOUNDS. Heart specialists have also shown that it is of
value to record the heart sounds on a moving strip of paper or film simultaneously with an
electro car diographic record. This dual record has proved an aid in the diagnosis of certain
cardiac disorders, and also for purposes of research into the mechanism of the heart.
23-12 MEDICAL APPLICATIONS OF ELECTRICITY
BIBLIOGRAPHY
Cabot, R. C., and H. F. Dodge, Frequency Characteristics of Heart and Lung Sounds, /. Am. Medical
Assoc., Vol. 84, 24 (June 1945).
Fletcher, Harvey, Speech and Hearing. Van Nostrand (1929) .
Frederick, H. A., and H. F. Dodge, The Stethophone, Bell Sys. Tech. J., Vol. 3, 531-549 (October 1924).
Gamble, C. J., and D. E. Replogle, A Multiple Electrical Stethoscope for Testing, J. Am. Medical Assoc.,
Vol. 82, 388 (February 1924).
Margolis, A., Archives of Internal Medicine, Vol. 46, 1048 (December 1930).
Rappapart, M. B., and H. B. Sprague, Graphic Registration of Heart Sounds, Am. Heart J., Vol. 23,
591-623 (May 1942).
Williams, H. B., and H. F. Dodge, Analysis of Heart Sounds, Archives of Internal Medicine, Vol. 38,
685-693 (December 1926).
ROENTGEN THERAPY
14. PURPOSE AND GENERAL TECHNICAL REQUIREMENTS
A short time after the announcement by Roentgen of the discovery of x-rays in 1895,
a number of physicians began to use the new radiation for the treatment of certain diseases.
It has been only since 1920, however, that important detailed data have been recorded and
correlated. It has been definitely determined that the absorption of x-rays by living
tissue can cause the destruction of that tissue. Destruction of a given type of tissue is
dependent upon the dose rate (in roentgens per minute; see below), the duration and
frequency of treatments, the area of the irradiated skin surface (portal), the total dose,
and probably other factors as well. The destructive action is radically different with dif-
ferent kinds of tissue. The reproductive cells of the human body are most sensitive, and
the bones are least affected. The treatment of malignant tumors, such as cancer, is based
upon the fact that, to a certain extent, it is possible to cause destruction of the diseased
tissue without permanently damaging normal surrounding tissue.
X-rays generated by means of a hot-cathode tube have continuous spectra character-
ized by a minimum wavelength dependent upon the maximum x-ray tube voltage. The
shorter the wavelength, the more penetrating is the radiation (see also Section 4, x-ray
tubes). For these reasons the kind of x-ray equipment chosen for therapeutic use de-
pends upon the site of the diseased portion which it is intended to treat. If, for example,
it is desired to treat the skin, it may prove desirable to use radiation of a wavelength of
the order of 1 A. Such radiations are sometimes called Grenz rays. The most generally
used x-ray therapy apparatus is operated at x-ray tube voltages of 50 to 400 kvp (peak
kilo volts). A filter consisting of a few millimeters of aluminum, a few tenths of a milli-
meter of copper, or a combination of the two, is inserted between the x-ray tube and the
patient. This filter absorbs a large part of the low-frequency radiation which would other-
wise be absorbed by the skin. The filtered x-ray energy penetrates to the site of disease,
and a reasonable proportion is absorbed and helps to produce the desired effect. Treat-
ments by x-ray therapy have been apparently beneficial in some cases, particularly if the
diseased part is properly diagnosed early in its development.
The gamma rays of radium have been valuable in treating cancer. It has therefore been
assumed that x-ray apparatus capable of generating radiation comparable in frequency
to gamma rays might prove useful. Experiments in this direction have led to the con-
struction of tubes and apparatus capable of operating at 600 kvp to 2 Mev.
APPARATUS. The high-voltage generator (50-400 kvp) required for exciting an
x-ray therapy tube is usually constructed with one of the following typical circuits as a
basis (see also Section 7, Power Supply) : (1) half-wave thermionic rectification; (2) special
half-wave rectified voltage-doubling circuits with condensers (see Fig. 1) ; (3) full-wave
thermionic rectification with condensers (nearly constant potential) .
Two kinds of apparatus have been devised and put into relatively common use for oper-
ation at 1 and 2 Mev.
In one of these devices a van de Graaff generator and an x-ray tube are assembled in a
steel tank into which air is introduced at a pressure of several atmospheres, the spark-
over potential gradient of gases at high pressures being considerably greater than at nor-
mal atmospheric pressure. The van de Graaff generator consists of a continuous belt of
insulating material mounted on two pulleys, one of which is at ground potential and is
driven by a motor. Near the bottom pulley electrodes are mounted in front of and in
back of the belt. A difference of potential is applied to these electrodes so that negative
charges (electrons) are deposited on the belt. Thus the moving belt effectively carries a
negative charge toward the top pulley. Surrounding this upper pulley there is mounted
ROENTGEN THERAPY
23-13
a hollow metal electrode to which a brush near the belt is connected. Electrons from the
belt are conducted to the exterior surface of the hollow electrode, which thus acquires a
negative charge. The cathode of the x-ray tube is connected to this upper electrode of
the generator; the anode of the tube is grounded. In order to maintain uniform potential
gradient throughout the length of the tube, cylindrical accelerating anodes are sealed into
the glass column of the tube and connected to taps on a resistor which in turn is connected
in parallel with the generator. The potential of the upper electrode with respect to ground
increases at the beginning of operation until the sum of the resistor current, the x-ray tube
£Uu T.U ,u6 !a1kage currents is equal to the rate at which charge is carried up on the
J-nus the tube operates at constant potential at voltages from 1 to 2 Mev, and
currents of the order of a few tenths milliampere are obtained.
The second type of equipment used for voltages above 1 Mev employs the same kind
of x-ray tube as the device described above but a different kind of high-voltage generator.
The generator consists of an auto transformer (air core) operating at 180 cycles per second.
FIG. 1. X-ray Therapy Apparatus, with Half-wave, Voltage-doubling Circuit
5. a-c leads; 6, auto-transformer; 8, a-c voltmeter; 9, exposure timer; 10. high-tension transformer;
13, thermionic valve; 14, d-o milliammeter; 15, x-ray tube of which 16 is the anode, 17, the cathode; IS,
cathode a-c ammeter; 19, the cathode heating transformer; 20, the cathode current regulator; and
27, the condenser.
The primary consists of a few turns of wire near the anode end of the tube wound coaxially
with the axis of the tube. The secondary consists of a series of coils (each connected to
an accelerating anode in the tube) mounted one above the other along the tube so that the
top coil is approximately at the level of the cathode of the tube. This apparatus is en-
closed in a steel tank into which "Freon" gas is pumped at a pressure of approximately 3
atmospheres.
15. TECHNIQUE
The x-ray tube mountings are arranged so that the patient may recline in a comfortable
position during treatment. A lead-lined cone protects the patient and operator from
scattered radiation. The radiation coming through the filter upon the patient is thus
confined to an area of 10-400 sq cm called a portal. Investigations have been made to
determine how much radiation is absorbed at various depths within the tissue. Sometimes
in order to get the desired absorption within a deeply seated tumor it is necessary to turn
the patient and to give several exposures through different portals, the central x-ray beam
passing, in each case, through the tumor. This method of cross-firing prevents the ab-
sorption in any particular skin area from exceeding a tolerable dose. The distance from
the tube to the patient is generally 50 to 100 cm. Tubes operate at currents of 5 to 30
ma, and the time of exposure may be from 5 to 45 min.
Just as with ultraviolet treatment, the individual tolerance must be investigated to
prevent x-ray burn. In general a large factor of safety is allowed to prevent such a pos-
sibility.
The unit of x-ray dosage is called the roentgen. It is denned in terms of measurement
by means of an ionization chamber. The roentgen is the quantity of x- or gamma-radia-
tion such that the associated corpuscular emission per 0.001293 gram of air produces (in
air) ions carrying 1 esu of quantity of electricity of either sign. It is assumed and ap-
parently justified by empirical results that this measurement parallels the biologic effect
of x-rays. The unit is an international standard. In some laboratories an ionization
23-14 MEDICAL APPLICATIONS OF ELECTRICITY
chamber is connected at all times; and in a few, the chamber operates an electric counter
which integrates the total dose and turns off the power supply to the x-ray tube after the
desired exposure. In other laboratories the x-ray machine is calibrated by means of a
sphere gap and a milliammeter which measure respectively the peak kilovoltage supply to
the x-ray tube and the average current through the x-ray tube. This calibration in turn
is referred to the results of ionization-chamber measurements made several times each
year.
BIBLIOGRAPHY
Charlton. E. E., W. F. Westendorp, G. Hotaling, and L. E. Dempster, New Million-volt X-ray Outfit,
J. Applied Phys., Vol. 10, 6, 374 (1939).
Duggar, B. A., Biological Effects of Radiation. McGraw-Hill (1936).
Glasser, Otto, Editor, Science of Radiology. Charles C. Thomas, Springfield, 111. (1933).
Glasser, Otto, L. S. Taylor, Edith Quimby, and J. L. Weatherwax, The Physics of Radiology. Hoeber
(1944).
Mayneord, W. B., The Physics of X-ray Therapy. Churchill, London (1929).
Robertson, J. K., Radiology Physics. Van Nostrand (1941).
van de Graaff, R. J., and J. G. Trump, Design of a Million-volt X-ray Generator for Cancer Treatment
and Research, J. Applied Phys., Vol. 8, 9, 602 (1937).
Weyl, Charles, S. R. Warren, Jr., and D. B. O'Neill, Radiologic Physics, Charles C. Thomas, Spring-
field, 111. (1941).
ROENTGENOGRAPHY AND ROENTGENOSCOPY
16. PURPOSE, GENERAL TECHNICAL REQUIREMENTS, AND
TECHNIQUE
In the first group of experiments performed by Roentgen the following x-ray phenomena
were observed.
• 1. X-rays, incident upon photographically sensitive emulsions, produced a latent image
similarly to visible light. Development of the emulsion produced a darkening of the film
or plate throughout the area traversed by x-rays.
2. X-rays, incident upon barium platino cyanide, produced a visible (fluorescent) radi-
ation.
3. X-ray absorption was greater for a given thickness of absorbing material in materials
of high density than in materials of low density. For a given absorbing material x-ray
absorption was found to be greater as the thickness increased.
These three facts form the bases of modern roentgenography.
The physically measurable characteristics of a roentgenogram of a part of the human
body which are most important for medical diagnostic purposes are: (1) roentgenographic
density; (2) roentgenographic contrast; (3) roentgenographic sharpness. Roentgeno-
graphic density and photographic density are identically defined as the logarithm to the
base 10 of the ratio of light incident upon a particular area of film to the intensity of light
transmitted through this area. Density is a function of x-ray intensity, therefore of x-ray
tube voltage, distance of the plate from the x-ray tube, current through the x-ray tube,
time of exposure, and of several less important factors, and also of the type of photographic
material and of the method of development and the fixing and drying of this material.
Density is, of course, a function of the physical characteristics of the object which is roent-
genographed. Roentgenographic density may be measured with a polarization photom-
eter or a photoelectric densitometer, or, for rougher approximation, densities may be com-
pared by eye. This last method is most unsatisfactory. Roentgenographic contrast is
the difference between the two densities of two areas of the roentgenogram and is there-
fore a function of the same variables as roentgenographic density. If it is desired to per-
ceive the difference produced roentgenographically by tissue of nearly similar x-ray ab-
sorption characteristics in the object roentgenographed, then it is important to control the
technique of roentgenography so as to make this difference clearly visible to the eye.
Roentgenographic sharpness is the ability of a particular roentgenographic equipment to
reproduce precisely borderlines between contiguous but definitely different densities. In-
formation deduced from the physical measurements of these characteristics is influenced
greatly by physiological and psychological factors associated with the viewing of roent-
genograms, which factors have not as yet been completely investigated.
In order to roentgenograph any particular part of the human body a tube having a very
Small focal spot is necessary. It is also advisable to remove the film and object from the
tube as far as possible in order to decrease distortion due to magnification of those parts o/
KOENTGENOGKAPHY AND BOENTGENOSCOPY 23-15
the object not in contact with the film. Since the focal spot of the x-ray tube is not a
point there will be some loss in roentgenographic sharpness due to its finite size. If the
object to be roentgeno graphed may be kept stationary for a moderately long period of
exposure, the focal spot may be made correspondingly small. This method is employed
for roentgenography of teeth and bones. If the part to be roentgenographed is con-
tinuously in motion a relatively short exposure is necessary, in order to arrest this motion
sufficiently. Therefore, to roentgeno graph parts such as the human chest the x-ray tube
focal spot must be made correspondingly larger in order to dissipate rapidly the energy
necessary for short exposure time. For roentgenography of the chest and heart, exposures
of 1/3o to */5 sec are used. For roentgenography of other parts of the body the exposure
time may be from 1/2 to 20 sec.
To control the contrast in the roentgenograms the voltage of the x-ray tube is varied.
The x-rays produced by high voltages are more penetrating than those produced by lower
voltages. The voltage of the x-ray tube is generally measured by means of a sphere gap
and is calibrated, for the particular current used, against the primary voltmeter reading.
The x-ray-tube current for exposures longer than 3 sec is measured by a d-c d'Arsonval
milliammeter. For very short exposures a ballistic milliampere-second meter is used to
measure the total quantity of electricity passing through the x-ray tube. The timer for
short exposures is arranged to make and interrupt the primary current at zero points of
the first and last half cycle of the exposure. The target-film distance is varied, depending
upon all the other factors involved; it generally has a value between 0.5 meter and 2 meters.
Secondary radiation from the heavier parts of the human body emanates in all direc-
tions, causing a general fogging effect over the whole area of the film and therefore reducing
the contrast so important for accurate diagnosis. To minimize this, the Potter-Bucky
diaphragm, consisting of a series of parallel lead strips perpendicular to the film and sep-
arated from each other by non-absorbing strips, is made to move over the surface of the
film during exposure. The lead strips effectively absorb cross-radiation (secondary radi-
ation) and therefore make better diagnostic results possible. Table 1 gives approximately
the techniques required for making roentgenograms of various parts of the human body.
Table 1. Technique for Roentgenography and Roentgeno scopy
Focal Spot-
X-ray Tube
X~ray Tube
Exposure
Intensi-
Purpose
film Distance,
Peak Volt-
Current
Time,
fying
meters
age, kvp
Average, ma
seconds
Screens
General roentgenoscopy . . . ,
0.5-1.0
60-90
2-10
20-60
Roentgenography
Hand
0.7-1.0
50-60
50
1.5
No
Elbow ,
0.7-1.0
40-60
50
1.5
No
Skull
0.7-1.0
60-75
100
I
Yes
Spine (use Bucky diaphragm) . . .
1.0
60-90
200
1
Yes
Colon (use Bucky diaphragm) . . .
1.0
60-90
100
1
Yes
Chest
1.25-2.0
45-85
30-500
0.4-0.033
Yes
17. APPARATUS
Roentgeixoscopic apparatus comprises simply a high-tension transformer with the
secondary connected directly to the x-ray tube (self-rectification) and a control apparatus
for adjusting the x-ray-tube voltage and current to predetermined values from 60 to 90
kvp and from 2 to 10 ma. Portable roentgenographic machines are usually self-rectified.
In order to avoid excessive voltage on the x-ray tube during the inverse half cycles, roent-
genographic apparatus for use at 30 to 500 ma makes use of thermionic rectifiers. Up to
100 ma, a single thermionic rectifier is connected in series with the x-ray tube, resulting in
half-wave rectification. At higher x-ray-tube currents (the usual ratings are 200 and 500
ma) , four thermionic rectifiers are connected in a bridge circuit to produce full-wave recti-
fiers. In addition there are a few roentgenographic machines using three-phase rectifiers;
there are also roentgenographic machines in which a high-voltage condenser with a ca-
pacitance of 0.25 to 1.0 juf is charged and subsequently discharged through the tube with
effective exposure times of less than l/io sec.
Several pieces of auxiliary equipment are essential for the production of good roentgen-
ograms. Generally the film is contained in a light-tight cassette having a front plate of
thin Bakelite or thin aluminum. Inside the cassette two intensifying screens, one on
either side of the film, are arranged to maintain close contact with the film when the cas-
sette is loaded. The x-rays passing through the screens excite fluorescence in the calcium
tungstate or zinc sulfide contained therein, and this fluorescent light radiation records
23-16 MEDICAL APPLICATIONS OF ELECTRICITY
upon the film. Screens now used produce about 95 per cent of the total roentgenographic
density, the other 5 per cent being caused by the direct absorption of x-rays in the film
itself.
Conventional techniques require the use of 14-in. by 17-in. films for a roentgenogram of
a chest. If it is desired to make chest films of many individuals, the cost is extremely
high. This has led to the development of photofluorographic equipment for making x-ray
surveys of the chest to discover early lesions of tuberculosis and other abnormalities. In
this apparatus the x-rays which have traversed the patient impinge upon a fluorescent
screen mounted in a light-tight box, opposite which a photographic camera is focused upon
the screen. The camera records the image from the screen on 35-mm or 70-mm roll film,
or on 4-in. by 5-in. flat film. Although the sharpness of the images of such photofluoro-
grams is inferior to the sharpness of a roentgenogram, the results are believed by many
radiologists to be accurate enough for surveys.
In order to standardize photofiuorographic techniques, an automatic timing device has
been developed. Light from a part of the screen is focused upon an electron multiplier
tube, the output of which is integrated and used to operate a switch to discontinue the
exposure at the end of the time required for producing the proper density on the film. This
automatic timing device is now being tested for possible application to standard roentgen-
ographic procedures.
The techniques of medical roentgenography have been increasingly used and further
developed in the examination of industrial products. Thus the equipment operating at
2 Mev is capable of producing a satisfactory record on x-ray film of steel as thick as 12 in.
The gamma rays from radium are also utilized to make films of metal parts. These are
extremely valuable methods of inspecting the industrial products in order to detect faults
within the product without destroying the product.
BIBLIOGRAPHY
McNeill, Clyde, Roentgen Technique. Charles C. Thomas, Springfield, 111. (1939).
Robertson, J. K., Radiology Physics. Van Nostrand (1941).
St. John, A., and H. R. Isenburger, Industrial Radiology. 2nd Ed., Wiley (1943).
Weyl, C., S. R, Warren, Jr., and D. B. O'Neill, Radiologic Physics. Charles C. Thomas, Springfield,
111. (1941).
18. MISCELLANEOUS DEVICES
Of the many electrical devices used in medicine that are not mentioned in the sections
above, three pieces of apparatus are briefly described in this section.
The electron microscope is a device in which a beam of electrons traverses a thin sample
of tissue or other material and impinges upon a fluorescent screen or film to produce an
enlarged image representing a pattern of the specimen. The electron beam is controlled
by means of electrostatic or electromagnetic lenses. The RCA type EMU is a recently de-
veloped commercially available electron microscope. The magnification can be varied
from 100 to 20,000; the resolving power is somewhat less than 100 A. The device operates
with a maximum difference of potential of 50 kvp. Films made on the electron microscope
can be photographically enlarged so that the overall magnification may exceed 100,000.
Among the limitations of the device are: (1) it is extremely difficult properly to prepare
specimens; and (2) the specimen may be destroyed or seriously modified in structure by
the electron beam.
The betatron is a device for accelerating electrons to velocities closely approaching the
speed of light. It consists of a laminated iron core with an air gap. Between the poles of
the gap there is mounted a doughnut-shaped vacuum tube into which pulses of electrons
with a duration of about 2 AISCC and velocities corresponding to approximately 80 kvp can
be injected into the evacuated space. A winding on the core is fed from a source of ISO-
cycle alternating current in order to produce across the air gap a magnetic field in which
the flux density varies sinusoidally with time; the first rising one-quarter cycle of the flux
(1/720 sec) actuates the device. The pulse of electrons is injected into the doughnut a few
microseconds after the magnetic flux has passed through zero and is increasing. Sub-
sequently, the increasing magnetic field causes the electrons to be accelerated; they trav-
erse the circular path within the tube several hundred thousand times in 1/720 sec. It is
possible so to shape the pole pieces that these electrons will remain in a stable circular
ofbit during their acceleration. At the end of the period (1/720 sec) they are caused to
spiral outward from the stable orbit and to impinge upon a target, causing the production
of x-rays. Betatrons for producing electron velocities corresponding to 20 Mev have been
in use for several years, and an experimental model of a 100 Mev betatron has been an-
HIGH-VOLTAGE SHOCK 23-17
nounced by the General Electric Company. At high equivalent voltages, some of the
phenomena observed in cosmic-ray studies have been produced in the laboratory for the
first time.
A cyclotron is a device for accelerating protons and heavier positive ions. Its operation
depends upon two facts: (1) charged particles traveling at right angles to a constant mag-
netic field traverse a circular path with constant linear velocity in the absence of an electric
field ; (2) charged particles are accelerated in the presence of an electric field in the direction
of their motion. Near the center of a shallow, cylindrical evacuated cavity, positive ions
are emitted from a suitable source at very low velocities. The cylindrical space is sur-
rounded by two semicircular dees, and the source of ions is located in the gap between the
dees. A source of high-frequency alternating voltage is applied to the dees so that those
positive ions that are emitted during the peak of a particular half cycle are accelerated
toward the dee which, at that instant, is negatively charged. Upon entering the dee the
effect of the electrostatic field becomes negligibly small, and the electrons would continue
in a straight line except that the dees are mounted in the gap between the poles of an
electromagnet excited by direct current. Thus the ions that have been initially ac-
celerated by their first traverse of the gap between the dees travel in a semicircle inside
the dees until they again reach the gap. The high-frequency source of potential between
the dees is adjusted so that the ion will be again accelerated as it crosses the gap the second
time.
This process is repeated, and the radius of the semicircle increases each time the ions are
accelerated by the electric field. Thus the ions spiral outward and are subjected to two
increases in acceleration during each revolution. After several hundred revolutions the
ions spiral outward to the maximum diameter of the dees and are then emitted tangentially
through a window. By placing various materials in the path of the beam outside the
cyclotron, important nuclear experiments can be carried out. For example, when protons
are accelerated in the cyclotron and permitted to impinge on beryllium, neutrons are pro-
duced in relatively large quantities. The largest of these devices, 184 in. in diameter, was
constructed at the University of California under the direction of Dr. E. O. Lawrence,
the inventor of the apparatus. The cyclotron has been used for many important experi-
ments in the phenomenal developments of nuclear physics. Note that the operation of the
cyclotron in its simplest form depends upon the following fact: The time required for ions
to move through one semicircle remains constant regardless of the linear velocity as long
as the velocity is not comparable with the velocity of light. Ions in cyclotrons with equiv-
alent voltages of 20 Mev or less satisfy the condition.
Several suggestions have been made of methods for accelerating both electrons and
positive ions to velocities corresponding to voltages of 10s or 109 volts, and development
of these methods is now proceeding.
BIBLIOGRAPHY
Electrical Engineering Staff MIT, Applied Electronics. Technology Press MIT and Wiley (1943).
Kerst, D. W., A 20-million Electron-volt Betatron or Induction Accelerator, Rev. Scientific Instrument s,
Vol. 13, 387-394 (September 1942).
Lawrence. E. 0., and M. S. Livingston, Production of High-speed Light Ions without the Use of High
Voltages, Phys. Rev. (Series 2), Vol. 40, 19-35 (April 1, 1932).
Schiff, L. L, Production of Particles beyond 200 Mev, Rev. Scientific Instruments, Vol. 17, 6-14 (Jan-
uary 1946).
HIGH-VOLTAGE SHOCK AND X-RAY BURN
19. HIGH-VOLTAGE SHOCK
The physiological effects of a high-voltage electric shock may be classified in two groups:
the major effects, such as cessation of respiration or heart action; and the less serious effects,
such as fractures and internal injuries due to falls, and also burns.
The first necessary action is to remove the victim, from the circuit without touching him
with bare hands. If it is not possible to open the circuit by means of a switch near at hand,
then it is usually effective to move the conductor, or the victim, with a non-conductor.
A physician should be summoned immediately, and it is important to administer first aid
or artificial respiration immediately while awaiting his arrival. If the victim is breath-
ing, heart stimulants may be administered hypodermically. The body should be rubbed to
produce external warmth, and the clothing should be loosened in order to excite con-
sciousness.
23-18 MEDICAL APPLICATIONS OF ELECTRICITY
If the victim does not breathe, artificial respiration should be applied as follows: Lay
the subject face down with arms and legs extended, and turn the face one side so that the
mouth and nose are free for breathing. Remove foreign bodies such as tobacco, gum,
and false teeth from the mouth, and have an assistant draw the subject's tongue forward.
Kneel, straddling the subject's thighs, facing his head; rest the palms of the hands on the
muscles of the small of the back with fingers spread over the lowest ribs. With arms held
straight, swing forward slowly so that weight is gradually brought to bear upon the sub-
ject. This operation should take 2 or 3 sec. Immediately swing backward, removing
the pressure. Repeat this procedure 12 or 15 times a minute, a complete respiration in
4 or 5 sec. Continue artificial respiration at least an hour without interruption or until
the physician arrives. Do not give any liquid by mouth until the subject is fully con-
scious. After the victim breathes again, shock treatment may be administered as out-
lined above. If any bones have been fractured or if the victim appears to have received
internal injury do not move him any more than is necessary and prepare for removal to
the nearest hospital.
If the victim has received burns the surface of the skin should be protected from the air.
Cut around any clothing that sticks to the burns and saturate adhering cloth or cotton
dressing with */2 per cent solution of picric acid or a solution of baking soda, about 1
teaspoonful to a pint of water.
BIBLIOGRAPHY
Dalziel, C, F., and J, B. Lagen, Effect of Electric Currents on Man, Sleet. Eng., Vol. 60, 63-66 (Feb-
ruary 1941).
Ferris, L, P., B. G. King, P. W. Spence, and H. B. Williams, Effects of Electric Shock on the Heart,
£Zec£.#ng., Vol. 55,498(1936).
20. X-RAY BURN
As noted under the section on roentgen therapy the effect of x-rays on living tissue is
always destructive. This effect is cumulative; that is, the successive application of small
doses may cause destruction of living tissues. Workers in x-ray laboratories should be
properly protected from exposure by the installation of lead or lead glass protective shields
about the x-ray tube. If the worker must be in the field of the x-rays, he should wear a
protective lead rubber apron, hood, and gloves. X-rays produced by low x-ray-tube
voltages are absorbed almost completely by the skin. To eliminate these x-rays, which
have normally no useful effect in treatment or roentgenography, a filter of !/2 mm or 1
mm of aluminum is placed between the x-ray tube and the patient.
The first effects of x-ray burn are reddening and itching of the skin and falling hair.
Later, open sores may develop, which may subsequently cause the destruction of large
areas.
Standards of x-ray protection have been set up and internationally accepted. These
standards should always be observed rigorously. It is necessary to make periodic tests by
having workers carry small pieces of light-protected film with a narrow lead strip covering
part of the outer casing. These films are carried over a period of several working days and
are then developed to discover whether any fogging has occurred on those portions of the
film not protected by the lead strip. Such fogging indicates the need of more effective
protective measures. lonization chambers, similar in shape and size to fountain pens,
may be charged and worn by a worker for several hours, and the exposure in fractions of a
roentgen may be measured by means of a calibrated electrometer. Although there is some
controversy concerning the magnitude of the safe daily tolerance dose, a commonly ac-
cepted value is 0.05 roentgen per day.
BIBLIOGRAPHY
X-ray Protection. Bureau of Standards, Handbook 20.
Protection against X-rays and Gamma Rays, Radiology, Vol. 46, 57-76 (January 1946).
American War Standard Safety Code for the Industrial Use of X-rays, Z54. 1-1946, Am. Standards
Assoc., New York.
INDEX
NOTE. The double numbers refer to both section and page numbers. For example, 1-38 indicates
page 38 of Section 1.
A board, 17-08
A.V.C., 7-125
A.W.G., 1-65, 1-68, 2-10
Ab, 1-43
Abamp, 1-46
Abamperes, conversion factors, 1-59
Abampere-turas, conversion factors, 1-64
Abbreviations for engineering terms, 1-71
Abcoulombs, 1-43, 1-44, 1-46
conversion factors, 1-58, 1-59
Aberrations, 14-11
eye, 14-29
Abfarads, 1-43, 1-46
conversion factors, 1-62
Abhenrys, 1-46
conversion factors, 1-63
Abmhos, 1-46
conversion factors, 1-62
Abohm-centimeters, conversion factors, 1-61
Abohms, 1-46
conversion factors, 1-61
Absolute, abbreviation, 1-71
altimeters, 22-32
coulomb, 1-43 fn
electrical system, 1-44
gain of directivity in antennas, 6-71
joule, 1-57
units of electrical measure, 1-44
Absorption coefficients, acoustical material, 12-48
measurement, 12-48
dielectric, in liquids, 2-51
in solids, 2-23
sound, see Sound absorption
Absorptivity, 12-40
Abvolts, 1-46
conversion factors, 1-60
A-c amplifiers, 21-16
equivalent circuit of vacuum tubes, 4-07
-operated receivers, filament power for, 7-106
power used for filament and plate supplies for
transmitters, 7-108
Acceleration, cgs unit, 1-46
conversion tables, 1-53
linear, conversion table, 1-53
mks unit, 1-46
of gravity, 1-53, 1-79
symbol for, 1-46
Acetone, 2-49
Acme, properties, 2-04
Acoustic design, auditoriums, 12-41, 12-69, 12-70,
12-71, 16-11
broadcasting studios, 12-41
court rooms, 12-41
motion-picture studios, 12-41
music rooms, 12-41, 12-74
theaters, 12-41 !
impedance of ear, 12-04
medium, effects, 13-02
physical properties, 13-02
reaction of, on a diaphragm, 13-02
radiators, 13-08
mechanical impedance to motion, 13-03
Acoustics, 12-02, see also Sounds
auditorium, 12-41, 12-69, 12-70, 12-71, 16-11
decay curves, 12-49, 12-50
domed ceilings, 12-70
ergodic state, of rooms, 12-41
geometric, 12-41
measure of reverberation, 12-48
good, practical procedure for obtaining, in
buildings, 12-76
procedure for obtaining, 12-76
requirements, 12-40
polycylindrical sound diffusers, 12-70, 12-71
properties of rooms, 12-39
echo, 12-40
effective sound pressure, 12-39
intensity level, 12-40
mean free path, 12-40
multiple echo, 12-40
noise, 12-40
pressure level, 12-39
rate of decay, see Acoustics, rate of decay
requirements for good, 12-40
reverberation, see Reverberation
sabin, 12-40
sound energy density, 12-40
sound intensity, 12-40
transmittivity, 12-40
velocity level, 12-40
rate of decay, 12-40, 12-48
curves obtained with high-speed level re-
corder, 12-49
high-speed level recorder, 12-49
non-linear, 12-49
ray, of rooms, 12-41
warble tone for reverberation measurements,
12-49
wave, 12-41
wave form produced at glottis in speech, 12-19,
12-20
Acre, abbreviation for, 1-71
-feet, conversion factors, 1-49
Acres, conversion table, 1-48
Acrylates, 2-34
Acrylic resins, 2-34
Active power, cgs unit, 1-46
mks unit, 1-46
symbol, 1-46, 1-73
Adaptation, light, 14-33
Adcock antennas, 6-87, 6-88, 22-06
Address systems, 16-14
Adequate coupling, 6-09
Adjacent-channel interference, in f-m systems,
8-30
Adjustable capacitors, 3-55
inductors, 3-52
resistors, 3-17
standards, 11-22, 11-23
Admittance, symbol, 1-72
Admittances, driving point, 5-07
mutual, 5-06
transfer, 5-07
Advance, properties, 2-04
INDEX
Aerotronics, 22-30
Age, effect of, on hearing, 12-07
Aging, 3-04
Air, 2-54
acoustic properties, 13-02
condenser, 3-53, 3-59
dielectric constant, 2-54
dielectric properties, 2-49
gap, 2-59, 3-45
minimum sparking potentials, 2-54
navigation, radio aids, 22-04
facilities in new federal airways system,
22-13
in federal airways system today, 22-06
landing systems, proposed, 22-26
long-range navigation systems, proposed,
22-31
miscellaneous, 22-31
short-range navigation systems, proposed,
22-28
terminology, 22-05
Air-core inductor, 3-31
transformers in circuits, 6-10
Airways, federal and civil, 22-02
Akbar, properties, 2-04
Alcomax, 2-66
Alexanderson alternators, 7-94
multiple-tuned antennas, 6-80
Alfer, 2-62, 2-70
Alferon, properties, 2-04
Alford loop antenna, 6-84
Algebraic formulas, 1-02
Alkyd resins, 2-34
Allocation, television frequency, 20-20
Alloy wires, of high tensile strength, 2-21
Alloys, aluminum-iron, 2-62
beryllium-copper, approximate values for the
physical properties, 2-11
cobalt-iron, 2-62
cobalt-platinum, 2-68
„ dispersion-hardening, 2-66
ductile, 2-68
for electrical resistance, 2-03
Heusler, 2-57
high-permeability, 2-61
iron-cobalt, 2-62
iron-nickel, 2-62
iron-silicon, 2-61
properties, 2-04, 2-09
All-pass network, 5-21
All-wave receivers, 7-124
Allyl resins, 2-34
properties, 2-26
Allymer, 2-34
Alnicos, 2-66, 2-67, 2-68
Alphabet, Greek, use for symbols, 1-79
Alsimag, 2-34
properties, 2-26
Alternating-current, abbreviation, 1-71
Alternators, 7-94
Alexanderson, 7-94
Goldschmidt, 7-94
Altimeters, absolute, 22-32
Altunel, properties, 2-04
Aluminum bronze, properties, 2-04
-iron alloys, 2-62
plates, 1-68
properties, 2-04, 2-10
sheets, 1-68
wire (tables), 2-17, 2-18
Alundum, properties, 2-10
Alvar, 2-34, 2-47
A-m receivers, f-m receivers and, 8-16
measurement, 11-43
A-m receivers, measurement, using standard test
loop antenna, 11-47
miscellaneous measurements, 11-50
Amber, 2-34
properties, 2-26
American Steel and Wire Co.'s gage, 1-69
Wire Gage, 1-66, 1-68, 1-69, 1-70
Zinc Gage, 1-66
Ammeter, graphical symbol, 1-76
Ammonium dihydrogen phosphate (ADP), 13-56
properties, 13-68
use in piezoelectric crystals, 13-56
useful cuts, 13-69
Ampere-hour, abbreviation, 1-71
-hours, conversion factors, 1-58
-turns, conversion factors, 1-64
Amperes, 1-43, 1-44, 1-45
abbreviation, 1-71
conversion factors, 1-59
Amphenol 912, 2-34
Amplification, see article on particular device
Amplification factor, 4-02, 4-13
defined, 4-06
variation, 5-45
Amplifiers, 7-02, see also Vacuum tubes
a-c, 21-16
audio, 16-06
of radio transmitters, 7-134
battery tubes used in combination for, 7-21
bidirectional, 7-13
booster, 16-09
bridging, 16-27
broad i-f , 7-60
cascade, 7-03
cathode follower, 7-31, 7-47, 7-48
class A, 7-02, 7-03
characteristics, 7-02
general use, 7-03
maximum plate power efficiency, 7-02
plate characteristics, 7-07
summary, 7-15
tube characteristics, 7-07
class AB, 7-02
class AB2, 7-02
class B, 7-02, 7-15
audio, dynamic transfer curves for a 1635
tube, 7-19
characteristics, 7-02
distortion, 7-23
frequency of grid currents, 7-18
input resistance, 7-17
low-power audio, 7-15
output circuit requirements, 7-18
plate efficiency, 7-16
plate loss, 7-16
power-output calculation, 7-16
radio, 7-22
summary, 7-24
theoretical maximum plate efficiency, 7-02
type 46, plate characteristics, 7-16
class C, 7-02, 7-24
apparent plate resistance, 7-26
characteristics, 7-02
circuit calculations, 7-24
circuit for increased efficiency, 7-26
efficiency of the plate circuit, 7-25
grid-leak method of supplying bias, 7-25
plate efficiency, 7-02
plate modulation and, 7-85
power calculations, 7-25
series tuned circuit, 7-88
summary, 7-27
typical circuit, 7-25
classes, 7-02
INDEX
Amplifiers, combined shunt and series peaked,
circuit, 7-37
plate load in terms of frequency and total
capacitance, 7-38
series inductance in terms of frequency and
plate load resistance, 7-39
shunt inductance in terms of frequency and
plate load resistance, 7-38
conditions for regeneration, 7-28
d-c, 21-16
defined, 7-02
direct resistance coupled, 7-04
Doherty, 7-131, 7-132
double-tuned circuits, 7-64
effects of regeneration, 7-28
electroacoustic equipment, 16-14
grounded-grid, 7-31, 7-49
harmonics of, 7-08
high-power, 7-136
high-power audio, 7-22
i-f, 7-56
as source of gain and selectivity in radio re-
ceiver, 7-58
broad, 7-60
coefficients of coupling, 7-59
critically coupled circuits, 7-59
double-tuned stage, 7-63
flat-topped selectivity curve, 7-59
for a-m broadcast receivers, 7-58
for f-m receivers, 7-61
medium bandwidth, 7-58
narrow bandwidth, 7-58
of superheterodyne receiver, 7-121
opposing couplings, gain and bandwidth of
i-f stage, 7-60
opposing inductive and capacitive coupling
and, 7-60
pulse technique, illustrated, 9-14
tuning stability, 7-60
variable selectivity of, 7-59
wide-band, 7-58, 7-63
in-phase, 7-31, 7-50
inverse feedback, stagger-tuned, vs., 7-70
inverse feedback i-f circuits, 7-68
klystron, 4-51
light-weight class B audio, 7-18
linear, 7-22
low-plate-resistance tube, 7-11
low-power audio, 7-15
low-power intermediate-r-f, 7-136
modulated, 7-75
motorboating of, 7-04
negative feedback, 7-31, 7-51
effect on distortion, 7-52
neutralization of grid-plate capacitance, 7-29
one-shot, 7-31, 7-53
oscillator buffer, 4-52
parasitic oscillation, 7-29
parasitic self-oscillation, 7-28
pentode audio power, distortion in, 7-13
pentode power, 7-13
pentode voltage, 7-11
power, 7-131
and efficiency of grid-bias-modulated, 7-73
negative feedback applied to, 7-133
plate-circuit modulation used in, 7-132
r-f harmonic radiation, 7-132
shunt neutralization employed in, 7-132
power amplification, 7-03
preliminary, 16-06
prevention of oscillation, 7-29
program, 16-09
pulse, see Pulse amplifiers
pushpull, 7-10
Amplifiers, radio, intermediate-r-f, 7-129
r-c coupled, 7-04, 7-90
regeneration in, prevention of, 7-28
repeaters, 7-15
response curve, 7-32
r-f, 7-22, 7-131
series peaked, 7-35
circuit for, 7-36
plate load in terms of frequency, 7-36
series inductance in terms of frequency and
plate load, 7-37
shunt peaked, 7-33
circuit for, 7-33
plate load in terms of frequency, 7-33
shunt inductance in terms of frequency and
plate load, 7-34
1635 class B audio, driver and output circuit
for, 7-20
special-purpose, 7-31
stagger-tuned, inverse feedback vs., 7-70
single-tuned circuits, 7-64
suppressor input, screen output, 7-51
synchronous single-tuned circuits, 7-64
synchronously tuned, overall band width of,
7-64
transformer-coupled, 7-05
output calculations, 7-07
transformer-coupled audio, input circuit calcu-
lations, 7-07
transformer-coupled class A, 7-07
triode power, 7-10
triode voltage, 7-10
tube, performance calculations from tube con-
stants, 7-09
plate efficiency, 7-09
power output, 7-09
tuned, 7-06
tuned coupling, 7-06
tuned-r-f receivers, 7-56
tuned-transformer-coupled, 7-06
uncompensated, plate load in terms of fre-
quency, 7-33
uncompensated amplifier stage, 7-32
unmodulated intermediate stages, 7-130
vacuum tube, effect of cathode resistor and by-
pass, 7-44
variable-gain pentode voltage, 7-12
variation of gain with frequency of resonance,
6-11
voltage amplification, 7-03
wide-band, 7-31
alternative designs, 7-64
circuit for, with constant-JC configuration
low-pass filter-coupling network, 7-40
consisting of three staggered triples, 7-67
double-tuned circuits used in, 7-64
figure of merit, 7-64
formulas, summary, 7-44
high-frequency compensation methods, 7-43
high-frequency response, 7-31
inverse-feedback amplifiers used in, 7-64
low-frequency response, 7-44
Miller capacitance effect of tubes, 7-43
peaking coil distributed capacity, 7-40
rise time of pulses, 7-64
stagger-tuned amplifiers used in, 7-64
synchronous single-tuned circuits used in,
7-64
video amplifier response curves, 7-42
with constant-jE-type coupling network,
7-39
wide-band i-f, feedback pair, 7-68, 7-69
feedback triple, 7-68, 7-69
Amplitude, distortion, 5-33
4
INDEX
Amplitude, modulation, 7-71
distortion due to incomplete rejection of,
8-27
distortion from, 8-28
frequency modulation converted to, 8-17
incomplete rejection of, f-m distortion and,
8-26
methods of producing, 7-72
-modulated radio transmitters, 7-129
Amp-turn, 1-46
Amyl acetate, dielectric properties, 2-49
Amyl alcohol, dielectric properties, 2-49
Analysis of sound, 11-65
Analyzers, commutated band, 11-66
'feedback, 11-60
heterodyne, 11-61
intermodulation, 11-61
machine noise, 11-63
requirements, 11-56
resonance, 11-58
suppression, 11-61
tuned-reed, 11-65
Anesthesia, local, 23-03
Angle, cgs unit, 1-46
current flow, 7-131
hyperbolic, 1-10
incidence, 5-53
mks unit, 1-46
plane, conversion table, 1-51
reflection, 5-53
solid, conversion table, 1-51
symbol, 1-46
trigonometric functions, 1-07
Angles of rectangular wave guides, 10-21, 10-22
Angstrom unit, abbreviation, 1-71
conversion factors, 1-47
international, 1-79
Angular acceleration, conversion table, 1-53
frequency, symbol, 1-73
localization of sounds, 12-18
velocity, cgs unit, 1-46
conversion table, 1-53
mks unit, 1-46
symbol, 1-46
Aniline, dielectric properties, 2-49
formaldehyde, power factor at high frequen-
cies, 2-34
-formaldehyde resins, 2-34
properties, 2-26
Annealed copper standard, 2-20
defined, 2-02
Anode current, defined, 4-05
defined, 4-04
dissipation, denned, 4-05
graphical symbol, 1-77
voltage, defined, 4-05
Anodes, 4-02
air cooled, 4-03
classification, 4-04
radiation cooled, 4-03
water cooled, 4-03
Antenna circuit, combination of capacitative and
inductive coupling, 7-115
Committee of the Institute of Radio Engineers,
6-88
coupling circuit of radio receiver, 7-115
coupling circuits, 7-116
effect, defined, 6-87
sensitivity of loop antenna to, 6-87
gain and bandwidths, 11-53
-testing methods, study of, 6-88
Antennas, see also Radio antennas
absolute gain of directivity, 6-71
absorption, 6-64
Antennas, Adcock, 6-87, 6-88, 22-06
Alexanderson multiple-tuned, 6-80
Alford loop, 6-84
antenna images, 6-69
aperture of arrays, 6-73
area efficiency factor of apertures, 6-76
array formed by stacking, 6-73
arrays, 6-64, 6-73
for broadcasting, 6-82
broadside, 6-72, 6-83
center of radiation, 6-65
Chireix-Mesney array, 6-65
circular, 6-85
classification, 6-64
cloverleaf, 6-85
collimating devices, 6-78
conical, input impedance, 6-66
cosecant, 6-87
of radar, 6-72
counterpoise, 6-69, 6-80
currents and voltages existing on, 6-66
curtain arrays, 6-83
cylindrical, input resistance, 6-67
cylindrical optics, 6-77, 6-86
ctipoles, electric and magnetic, directional dia-
gram of, 6-70
direction finding of, 6-87
directional, 6-71
a-m broadcasting, 16-29
use of, in medium-frequency broadcasting,
6-74
directional diagrams of isolated wires, 6-75
directivity of, effect of soil and terrain, 6-74
directivity of broadcast transmitting, 6-74
dummy, defined, 11-51
effective area, 6-72
end-fire array, 6-72
field intensity and loop in free space, 6-70
field intensity, 6-70
fields associated with, 6-69
flat-top, 6-80
folded wire arrays, 6-83
for aircraft, 6-88
for broadcast reception, 6-82
for high frequencies, 6-82
for low frequencies, 6-80
for medium-frequency broadcasting, 6-81
for very high and ultra high frequencies, 6-84
forms of, 6-63
Franklin arrays, 6-65
free space transmission law, 6-72
front feed for reflectors, 6-86
graphical symbol, 1-76
ground systems and, 6-69
grounded-quarter-wave, 6-70
half-wave, 6-70
hollow cylindrical, input reactance, 6-67
horizontal, directional diagram of, as influenced
by finite conductivity of earth, 6-75
inverted- V, 6-83
lenses, 6-78
line sources of wavelength power, 6-77
linear arrays, 6-64
linear conductor, 6-64
directivity, 6-73
principles, 6-65
long-wire, 6-64
loop, 6-85
graphical symbol, 1-76
sensitivity to antenna effect, 6-87
magnetic currents, 6-64
microwave, 6-86
primary feed, 6-77
radiation, 6-77
INDEX
Antennas, microwave lobing, 6-87
Musa receiving, 6-83
diversity reception, 6-83
non-directional, 6-71
using horizontal polarization, 6-85
non-dissipative, aperture, 6-76
effective area, 6-76
omnidirectional, using vertical polarization
6-84
optics of, cylindrical, 6-77
spherical, 6-77
parabolic reflectors, 6-78
paraboloid, beam width, 6-76
I nomogram, 6-76
•wavelength, 6-76
point sources of wavelength power, 6-77
practical systems, 6-80
pylon, 6-86
quarter-wave, 6-70
quasi-optical, 6-63
directivity, 6-76
lenses, 6-78
quasi-optical devices, 6-64
radiated power from vertical grounded wire,
6-70
radiation efficiency, 6-68
radiation from, 6-64
radiation resistance, 6-68
RCA broadside arrays, 6-65
rear feed for reflectors, 6-86
reciprocity, 6-64
reflectors, 6-78
resistance, 6-68
resonant, 6-81
resonant-V, 6-83
rhombic, 6-64, 6-83
rocket, 6-85
scanning method, 6-87, 6-88
shielded loop, 6-87
short-wave, locations, 6-75
shunt-fed, 6-81
simple, components forming total resistance,
6-68
equivalent circuit, 6-67
vertical quarter-wave, 6-70
single vertical, directional diagram, 6-71
sterba array, 6-65, 6-82
tower, 6-81
transmission lines and, 6-88
transmitting, a-m broadcasting, 16-28
f-m broadcasting, 16-29
turnstile, 6-84
typical arrays, 6-65
unidirectional broadside arrays, 6-73
unidirectional couplet, 6-73
unzoned lens of reflectors, 6-78
V-antenna, 6-64
vertical grounded wire, field intensity, 6-70
vertical half-wave, directional diagram of, as
influenced by finite conductivity of earth,
6-75
voltage induced in, 6-69
wave, 6-64
wave-guide, 6-64
zoned lens of reflectors, 6-78
zoning of waves by lens, 6-79
Anticathode, 4-81
Anti-hyperbolic sine, 1-10
Antimony, properties, 2-04, 2-10
Anti-sine, 1-08
Apartments, noise levels acceptable in, 12-58
sound insulation in, 12-57
Aperiodic disturbances, 5-28
Aperture distortion, 19-07, 20-30
Aperture distortion, of arrays, antennas and, 6-73
of non-dissipative antenna, 6-76
Apothecaries' fluid measure, conversion factors,
1-50
weight, conversion table, 1-55
Approximations, mathematical, 1-16
Arbitrary constants, 1-13
Arc, conversion factors, 1-48
defined, 4-58
graphical symbol, 1-76
resistance, 2-24
Arc-back, 4-62
Architect's measure, conversion factors, 1-48 |
Are, 1-48
Area, cgs unit, 1-46
conversion table, 1-48
efficiency factor of apertures of antennas,6-76
mks unit, 1-46
of segment, 1-18
symbol, 1-46
Argentan, properties, 2-04
Argon, dielectric constant, 2-54
Arithmetical progression, 1-02
Armite, 2-34
Aroclors, 2-34
Arrays of antennas, 6-64, 6-73
Arrester, lightning, graphical symbol, 1-76
Arsenic, properties, 2-04
Articulation, 12-27
clipping, effects, 12-34
delay, effects, 12-36
extraneous noise, effects, 12-33
frequency shift, effects, 12-35
non-linear distortion, effects, 12-34
percentage, curves for rooms of different sizes
and different times for reverberation, 12-74
for rooms, 12-69
phase distortion, effects, 12-35
resonance type of frequency distortion, effects,
12-33, 12-34
room reverberation, effects, 12-38
tests, 12-31
Artificial ear, 12-04
larynx, 12-21
respiration, 23-18
voice, 12-21
Asbestos, 2-34
ebony, 2-35
paper, 2-35
properties, 2-26
textiles, 2-35
wood, 2-35
Ascoloy, properties, 2-04
Askarels, 2-52
Aspect ratio, 20-03, 20-20
Asphalt, natural, 2-35
petroleum, 2-35
properties, 2-26
relation between dielectric constant and resis-
tivity, 2-51
sulfurized, 2-35
Asphaltites, 2-35
Astigmatism, 14-12
Atmosphere, abbreviation, 1-71
conversion factors, 1-56
Atmospheric noise, 10-42, 10-48
pressure, 45 deg cent, 1-79
normal, 1-79
Atomic weight, abbreviation, 1-71
Attenuating band, of filters, 6-33
Attenuation characteristic (Tchebycheff type) of
symmetrical filter, 6-56
constant, symbol, 1-72
equalizer, 16-28
6
INDEX
Attenuation, measurements, 11-82
minimum, 5-12, 6-57
Attenuator sections in passive circuits, 6-05
Attenuators, 3-20
design, 11-99
Audible effects of phase distortion, 9-34
field, 12-05
frequency ranges of music, speech, and noise,
12-30
methods used in frequency measurement, 11-09
pressure, 12-05
Audio amplifiers, 16-06
of radio transmitters, 7-134
feedback factor, 11-48
-frequency analysis, 1 1-65
-frequency transformers, see Transformers, au-
dio-frequency
Audiograms, 23-11
Auditoriums, acoustic design, 12-41, 12-69, 12-70,
12-71, 16-11
noise levels acceptable in, 12-58
sound level of speech for, 12-73
Auditory magnitude of sound, 12-11
nerve fibers, 12-03
nerves, 12-02
excitation of, 12-03
conduction of neural pulses to brain, 12-04
pitch of low-frequency tones and, 12-03
ossicles, 12-02
perspective of sounds, 12-39
range, 12-09
sensation area, 12-09
Aural, radio range, 22-06
-visual range, 22-08
Austin-Cohen formula (sky wave propagation),
10-39
Automatic direction finder, 22-04
flight, 22-05
and landing equipment, 22-22
volume control, effect on the fidelity of receiv-
ers, 7-125
A.V.C., 7-125
Average, abbreviation, 1-71
hearing loss, 12-08
Avogadro's number, 1-79
Avoirdupois, abbreviation, 1-71
weight, conversion factors, 1-54, 1-55
A.W.G., 1-65, 1-68, 2-10
Axes, crystalographic, 13-59
Ayrton-Perry coil, 11-19
B board, 17-08
& S gage, 1-67, 2-12
supply circuit, 7-106
pl unit, 1-38
Babbitt permeameter, 2-74
Back porch, 20-16
-wall effect, 15-13
Bactericidal radiation, 23-07
Baffle, 13-11
Bakelite, 2-35
Copolymer Resins, 2-39
resin, properties, 2-26
Balanced armature speaker, 13-15
discriminator, f-m distortion and, 8-28
power circuit, 10-77
response to amplitude modulation, distortion
and, 8-28
Balata, 2-35
Ballast lamps, 3-22
tubes, 4-08
Balsa wood, 12-51
Balsam wool, 12-53
Band frequency analyzer, 11-60
Band speaker, 13-11
Band-pass filter, 6-33
illustrative design, 6-59
mechanical, 11-63
Bandwidth, 5-32
inadequate, f-m distortion and, 8-26
television, 20-04, 20-06
Bank winding, 3-31
Banking rooms, noise level acceptable in, 12-58
Bar, conversion factors, 1-56
Barium titanate, properties, 2-30
Barkhausen effect, 2-69
Barkhausen-Kurz Oscillator, 7-91
Barometer, abbreviation, 1-71
Barrel, abbreviation, 1-71
Barrier photocells, 15-13
frequency response, 15-15
illumination response, 15-13
sensitivity, 15-14
structure, 15-13
wavelength response, 15-13
Baryes, conversion factors, 1-56
Base of natural logs, 1-19
Bass viol, power, 12-25
Battery, graphical symbol, 1-76
tubes, used in combinations for amplifiers, 7-21
Baume, abbreviation, 1-71
Beacon, non-directional, defined, 22-05
omnidirectional, defined, 22-05
Beads, 20-04
Beam coupling coefficient, 4-53
transadmittance, 4-53
transconqluctance, 4-53
width of paraboloid antenna, 6-76
Bearing, defined, 22-05
Beat frequency indicator, 11-05
frequency oscillator, 7-89
methods used in frequency measurement, 11-06
Beatnote interference, in f-m systems, 8-29
Beeswax, 2-35
properties, 2-26
Beetle, 2-35
Bel, 1-37
Bellini-Tosi loop method of direction finding, 6-88
Benalite, 2-39
Bends, defined, 22-06
of rectangular wave guides, 10-21, 10-22
Benzene, dielectric properties, 2-49
relation between dielectric constant and resis-
tivity, 2-51
Beryllium-copper alloys, approximate values for
the physical properties of, 2-1 1
properties, 2-04
Bessel function in frequency modulation, 8-08
zero, values of, for first 180 modes in circular
cylinder resonators, 7-104
Bessel functions, 1-37
chart, 1-37
in frequency modulation, 8-04
values, 8-05
BessePs equation, 1-15
Betatron, 23-16
Bias, 4-06
Bidirectional amplifier, 7-13
Binaural hearing, 16-02
minimum audible sound field intensity levels
in hearing, 12-06
reproduction, 12-39
Binocular television, 20-67
vision, 14-46
Biotite, 2-39
"Birdies" in intermediate frequencies, 7-57
Birmingham Gage, 1-66
Wire Gage, 1-66, 1-69, 1-70
INDEX
Bismuth, properties, 2-04, 2-10
Black body, 15-29
level, 20-13, 20-21
Blanking, 20-17
Blocked impedance, 5-65
Blocking oscillators, 9-18
pulse duration and, 9-20
repetition rate of pulses determined by, 9-19
Blood pressure, 23-08
Blurring interference, 12-70
Board measure, conversion factors, 1-49
Boiling point, abbreviation, 1-71
Bolometer, 15-04=
bridge, 9-11
circuits, 11-79
detector, 11-77
thermistor, 15-04
Bolometric methods, for low-power measure-
ments, 11-77
Boltzmann constant, 1-79
Booster amplifier, 16-09
Bootstrap circuit, 20-10
Boron, properties, 2-04, 2-10
Bougie decimales, conversion factors, 1-65
Bracket, square cross, 5-43
Brake horsepower, abbreviation, 1-71
-hour, abbreviation, 1-71
Brass plates, 1-68
properties, 2-04, 2-10
sheets, 1-68
Breaking load, for solid wires, 2-21
Brick, 12-65
Bridge methods, 11-12
networks, 5-13
Bridging amplifier, 16-27
Briggsian logarithms, 1-19
Brightness, cgs unit, 1-46
mks unit, 1-46
symbol, 1-46
television, 20-03, 20-21, 20-66
Brinell hardness number, abbreviation, 1-71
British bushel, 1-50
gallon, 1-50
Imperial pound, 1-42
Imperial yard, 1-42
Standard Wire Gage, 1-69, 1-70, 2-14
thermal unit, abbreviation, 1-71
conversion factors, 1-57, 1-64, 1-65
Broadcast coverage, range, 10-47
frequency allocation, 16-30
practices, 16-25
receivers, 11-43
average stage gains and second detector sen-
sitivities for different types produced be-
tween 1934 and 1946, 7-59
system, dynamic volume range, 16-34
layout, 16-26
tonal range, 16-33
Broadcasting, frequency modulation, 16-31
coverage, 16-32
high-frequency, 16-31
radio telephone, see Radio telephone broad-
casting
standard, 16-30
coverage, 16-32
station service, 16-32
continuity of, 16-33
interference, 16-33
studios, acoustic design, 12-41
sound insulation, 12-57
television, 20-21
transmitter plant, 16-28
Broadside array antennas, 6-72, 6-83
Bronze, properties, 2-04
Brown and Sharpe wire gage, 1-66
Btu, 1-57, 1-65
Buffer capacitor, of transformers, 6-31
Buildings, calculations of insulation in design,
12-69
industrial, sound insulation, 12-57
office, sound insulation, 12-57
Build-up time, 5-35
Buna N, 2-35
S, 2-35
Burn, x-ray, 23-17
Burrows permeameter, 2-74
Bushels, British Imperial, conversion factors, 1-50
dry, conversion table, 1-49
heaped, conversion factors, 1-50
struck, conversion factors, 1-50
U. S., conversion factors, 1-49, 1-50
II. S. Winchester, 1-50
Busy test, 17-08
Butacite, 2-35, 2-47
Butt treatment, 10-54
Butvar, 2-35, 2-47
Butyl, 2-35
stearate, dielectric properties, 2-49
Buzz tone in speech, 12-21
Buzzer output, 11-65
BWG, 1-69
Cable Morse Code, 18-04
Cables, 10-56
coaxial, 10-57
conversion factors, 1-47
length, 1-47
loading coils, 10-58
sheath corrosion, 10-63
principal causes, 10-63, 10-64
remedial measures, 10-65
sheath protection, 10-57
spiral-four disk-insulated, 10-57
Cadmium, properties, 2-04, 2-10
Calcite, effective grating space, 1-79
Calcium, properties, 2-04
titanate, properties, 2-30
Calculus formulas, 1-12
Calido, properties, 2-04, 2-10
Calorie, abbreviation, 1-71
Calorimeter hi pulse measurements, 9-12
Calorimetric methods, for high-power measure-
ments, 11-81
Calorite, properties, 2-04
Camera, television, 20-23
Cancer, 23-12
Candle, 1-43, 1-46
abbreviation, 1-71
-hour, abbreviation, 1-71
International, 1-43, 1-65
Candlepower, abbreviation, 1-71
mean horizontal, abbreviation, 1-72
spherical, abbreviation, 1-72
Candles, English, conversion factors, 1-65
German, conversion factors, 1-65
International, conversion factors, 1-65
Capacitance, distributed, of audio-frequency
transformer winding, 6-24
electrical, cgs unit, 1-46
conversion table, 1-62
mks unit, 1-46
symbol, 1-46
electrode, denned, 4-06
electrostatic, 1-72
formulas, 3-57
input, defined, 4-06
interelectrode, 4-14
denned, 4-06
8
INDEX
Capacitance, measurement, 11-24
audio-frequency transformers, 6-25
output, defined, 4-06
standards, 11-20
symbol, 1-72
variation, 5-41
Capacitivity, relative, symbol, 1-72
space, cgs unit, 1-46
mks unit, l-46f
symbol, 1-46
symbol, 1-72
Capacitors, 3-53
adjustable, 3-53, 3-55
air, plate spacing, 3-59
capacitance formula, 3-57
ceramic dielectric, 3-67
characteristics, 3-54
classification, 3-53
effect of stray capacitance, 3-56
electrolytic, 3-54, 3-68
fixed, 3-53
classified according to dielectric medium, 3-53
classified according to plate structure, 3-54
graphical symbol, 1-76
shielded, graphical symbol, 1-76
impregnated-paper, 3-53, 3-60
metalized paper, 3-64
mica, 3-64
solid-dielectric, 3-53
variable, 3-53, 3-55
graphical symbol, 1-76
shielded, symbol, 1-76
Capacity, see Capacitance
Carat, conversion factors, 1-54
Carbon dioxide, dielectric constant, 2-54
dielectric properties, 2-49
minimum sparking potentials, 2-54
grains, properties, 2-10
microphone, 13-26
monoxide, dielectric constant, 2-54
powder, properties, 2-10
properties, 2-04, 2-10
resistors, 3-11
steels, 2-66
tetrachloride, dielectric properties, 2-49
Carbonyl iron, 2-62
powder, 2-64
Carcels, conversion factors, 1-65
Cardiography, 23-08
Cargo, measurement of, conversion factors, 1-50
Carrier, effect of shift, 12-35
frequencies, 10-04
telephone systems, 17-43
wave of modulation, 7-70
Cascade amplifiers, 7-03
cavity, 4-53
Casein, 2-35
plastic, properties, 2-26
Castor oil, 2-52
dielectric properties, 2-49
relation between dielectric constant and resis-
tivity, 2-51
Catalin, 2-35
Cataphoresis, 23-03
Catenary, equation, 1-05
Cathode current, defined, 4-05
for long pulses in vacuum tubes, 9-26
dark space, 4-59
follower (amplifier), 7-31, 7-47
line matching, 7-48
heating time, 4-08
-lead inductance, 4-16
• lenses, 14-58
-ray devices, scanning circuits, 20-08
Cathode -ray oscilloscopes, 2-76, 11-07
-ray tube, 4-02, 15-41, 20-08
bulbs, 15-43
defined, 4-04
displays, 15-49
for magnetic deflection, graphical symbol,
1-77
oscillograph-type, 15-47
defined, 4-04
high-frequency deflection, 15-47
scanning circuits for, 20-08
screens, 15-37
television picture-reproduction, 15-46
traces on, photography of, 15-45
with electrostatic deflection, graphical sym-
bol, 1-77
spot, defined, 4-75
Cathodes, classification, 4-03
cold, graphical symbol, 1-77
defined, 4-04
directly heated, 4-03
graphical symbol, 1-77
filamentary, 4-08
indirectly heated, 4-03
graphical symbol, 1-77
ionic-heated, with supplementary heater,
graphical symbol, 1-77
material, 4-03
photoelectric, graphical symbol, 1-77
pool, graphical symbol, 1-78
thermionic, 4-02
unipotential, 4-08
Cathodoluminescence, defined, 15-30
Cauterization, 23-03
Cavity modulation in speech, 12-19
resonators, 7-95, 11-13
cavity couplings, 7-103
circular cylinder, 7-97, 7-99, 7-101
coupling by means of electron beam, 7-106
degeneracy in circular cylinder, 7-101
design of high-Q cavity in TE Oln mode,
7-103
elliptical cylinder, 7-101
formulas, 7-96
full coaxial cylinder, 7-98, 7-101
mode chart for circular cylinder, 7-102
modes, 7-101
orifice coupling of wave guide to cylindrical,
7-105
principle of similitude, 7-101
right rectangular cylinder, 7-96, 7-99, 7-101
Ceiling isolator, sound insulation and, 12-60
radio, 10-37
Ceilings, domed, reflection of sound from, 12-70
Ceilometer, 22-13
Celeron, 2-36
Cellophane, 2-35
Cells, cesium oxide, 15-18
choice of, for various purposes, 15-15
photoconductive, see Photoconductive cells
photoemissive, see Photoemissive cells
photovoltaic, 15-15
Celluloid, 2-35, 2-36
properties, 2-26
Cellulose acetate, 2-35
-butyrate, 2-36
power factor at high frequencies, 2-34
properties, 2-26
nitrate, 2-36
properties, 2-26
propionate, 2-36
properties, 2-26
Celotex, compliance and resistance data in insula-
tion of vibration, 12-62
INDEX
9
Centiare, conversion factors, 1-48
Centigrade, conversion table, 1-64
units, 1-43
conversion table, 1-64
Centigram, abbreviation, 1-71
conversion factors, 1-54
Centiliter, abbreviation, 1-71
conversion factors, 1-49
Centimeter, 1-63
abbreviation, 1-71
conversion table, 1-47
cubic, abbreviation, 1-71
conversion table, 1-49
-dynes, conversion factors, 1-57
-gram-second (system), abbreviation, 1-71
-grams, conversion factors, 1-57
square, abbreviation, 1-72
conversion table, 1-48
Centimetric waves, 1-SO
Ceramic capacitors, 3-67
Ceramics, 2-36
Ceresin, 2-36, 2-41
wax, properties, 2-26
Cerex, 2-36
properties, 2-26
Cesium oxide cells, 15-18
properties, 2-04
cgs electromagnetic system, 1-43
electrostatic system, 1-43
Chain, square, conversion factors, 1-48
Chain (Gunther's), conversion factors, 1-47
Characteristic (of logarithm) , 1-19
curves, vacuum tubes, 4-31
electrode, 4-06
impedance, 10-03
of speech sounds, 12-20
Charge density, symbol, 1-72
electric, symbol, 1-72
electronic, 1-79
line d. of, abbreviation, 1-72
of electron, 1-79
per unit area, conversion table, 1-59
Chatterton's Compound, 2-36
Chemaco, 2-37
Chemically pure, abbreviation, 1-71
Chemigum, 2-35
Chestnut poles, 10-53
Cheval-vapeur, 1-58
China wood oil, relation between dielectric con-
stant and resistivity, 2-51
Chlorinated diphenyl, dielectric properties, 2-49
Chlorobenzene, dielectric properties, 2-49
Chloroform, dielectric properties, 2-49
Choke feed, 7-08
input filter, 7-108
swinging, 3-48
Chromax, properties, 2-04
Chrome steel, 2-63
Chromel, properties, 2-04
Chromium,, properties, 2-04
Chronin, properties, 2-04
Chronograph, 11-04
Churches, acoustic design, 12-41
noise levels acceptable in, 12-58
sound insulation in, 12-57
Cibanite, 2-34
Cimet, properties, 2-04
Circle, equation, 1-05
mensuration, 1-18
Circuit Q of unmodulated intermediate amplifier
stages, 7-130
Circuits, see also Networks
air-core transformers, 6-10
antenna coupling, 7-116
Circuits, antenna coupling, of radio receiver, 7-115
bootstrap, 20-10
butterfly tuning, 11-90
cathode-ray devices, 20-08
clamp, 20-16
clock, 18-40
coupled, see Coupled circuits
deflection, 20-08, 20-10
electric, 5-02
electronic control, 21-13
electronic power, 21-02
elements, 6-02
envelope delay distortion measuring, 11-35
for measuring static characteristics, 4-08
impedance bridge in, 6-12
inverse feedback i-f amplifier, 7-68
linear, 5-37
measurement, conductance, 4-12
electrode capacitance, 4-14
Mu factor, 4-13
transconductance, 4-12
neutralizing, 6-12
non-linear, 5-37
approximate series expansion for plate cur
rent of a triode, 5-41
capacitance variation, 5-41
characteristics of triode with load, 5-42
current-voltage characteristic, 5-38
harmonic analysis of current for a sinusoidal
applied voltage, 5-46
inductance variation, 5-40
multi-electrode tubes, analyses for, 5-45
power series solution, 5-38
solution, 5-38
successive approximations, 5-45
trigonometric series, 5-39
parallel, resonance, 6-04
passive, attenuators, 6-05
complex coupling, 6-07
elements, 6-02
pads, 6-05
phase-measuring, 11-34
pulse, see Pulse circuits
pulse shaping, see Pulse shaping circuits
pulse timing, see Pulse timing circuits
receiver, see Receiver circuits
rectifiers, 7-110
wave form in, 7-107
regulating, 21-17
relaxation, see Relaxation circuits
semi-butterfly, 3-57
series resonant, 6-02
simple series, variation of current with fre-
quency in, 6-03
variation of voltage components with fre-
quency in, 6-03
single-mesh, 5-02, 5-03, 6-02
circuit Q, 6-04
dipoles in, 6-05
elements of attenuator sections, 6-05
matched impedances in, 6-06
non-matched impedances in, 6-06
quadripoles in, 6-05
series resonant, 6-02
T section attenuator in, 6-06
T sections in, 6-06
voltage relations, 6-02
thyratron grid-control, 21-19
timing, 21-14
transmission, 10-02
-frequency characteristic, 6-02
of two single circuits in cascade, 6-10
transmitter, for f-m transmitters, 8-15
tuned amplifier, 6-11
10
INDEX
Circuits, Wheatstome bridge, 4-11
wire transmission, see Wire transmission lines
Circular, abbreviation, 1-71
antennas, 6-85
cylinder cavity resonator, 7-97, 7-99, 7-101
mode chart, 7-102
inch, conversion factors, 1-48
mil, abbreviation, 1-71
conversion factors, 1-48
wave guides, 10-13
Clamping or d-c reinsertion of pulse shaping cir-
cuits, 9-17, 20-16
Clapping, 12-30
Clarinet, power of, 12-25
Class A amplifier, 7-02
B amplifier, 7-15
C amplifier, 7-24
Classrooms, noise levels acceptable in, 12-58
Clearance, defined, 22-05
Climatic loading, 10-51
Climax, properties, 2-05
Clipping, effect of, 12-34
Clock circuits, 18-40
synchronons, 11-04
Close-tolerance resistors, 3-06
Cloth, varnished, 2-47
Cloverleaf antennas, 6-85
Coaxial cables, 10-57
lines, 10-05, 10-09 i
Cobalt-iron alloys, 2-62
-platinum alloys, 2-68
properties, 2-05
steels, 2-66
Co-channel interference in f-m systems, 8-30
Cochlea of ear, 12-02
basilar membrane, 12-03
canals, 12-03
scala media, 12-03
scala typani, 12-03
scala vestibuli, 12-03
lamina spiralis ossea, 12-03
nerve, 12-03
semi-diagrammatic section, 12-03
Codes, color, 3-12
telegraph, 18-02
Coefficient, abbreviation, 1-71
absorption, 12-48
decrement, of couplings, 6-09
transmission, 12-63
coupling, symbol, 1-72
resistance-temperature, symbol, 1-73
Coercive force, defined, 2-59
Coercivity, defined, 2-59
Coil, 3-31
constant, 10-21
Cold cathode, graphical symbol, 1-77
Cold-cathode tubes, 4-72
available types, 4-75
test, 4-74
Collimating devices of antennas, 6-78
C ©logarithm, abbreviation, 1-71
Color (colors), 14-35
adaptation, 14-39
chromaticity diagram, 14-38
code, 3-12
hue discrimination threshold, 14-36
sensation, 14-35
specification, 14-37
stimulus, 14-35
television,. 20-65
tolerance, 14-39
Colpitts oscillator, 7-83
Coma, 14-12
Combinations, 1-03
Comet, properties, 2-05
Common logarithms, 1-19
abbreviation, 1-71
year, conversion table, 1-51
Communication systems, coordination of power
and, 10-67
Comol, 2-66, 2-67
Comparison measurements, 11-27
Compatability, 20-66
Compensated volume control, 7-126
Compensation theorem, 5-12
Complementary impedances, 5-10
Complex frequency plane, 5-04
notation, 5-03
quantities, 1-OC
Compliance, 5-57
Composition carbon resistors, 3-11
Compound coupling, tuned r-f tiansformer em-
ploying, 6-11
Compressive strength, 2-26
Computers, flip-flop circuits, 9-13
two-digit decade counter, 9-09
Concentrate, abbreviation, 1-71
Concentric tube line, 10-09
Concrete, acoustics of, 12-66
Condenser constant, 11-21
electrolytic, 3-68
fixed, graphical symbol, 1-76
input filter, 7-108
microphone, 13-24
speaker, 13-16
Conductance, electrical, cgs unit, 1-46
conversion factors, 1-61
mks unit, 1-46
symbol, 1-46, 1-72
measurement circuit, 4-12
measurement, 11-24
minimum, 5-08
of an electrode, 4-1 1
Conducting materials, 2-02
definitions, 2-02
specific, properties, 2-03
wire tables, 2-12
Conduction, gaseous, 4-58
nerve, see Nerve conduction
Conductivity, abbreviation, 1-71
denned, 2-02
effective, defined, 2-02
electrical, cgs unit, 1-46
conversion table, 1-62
mks unit, 1-46
symbol, 1-46
equivalent, symbol, 1-72
of gases, 2-54
of liquids, 2-50
symbol, 1-72
thermal, conversion table, 1-65
units of, defined, 2-02
Conductor, 1-76
Conduit, underground, 10-58
Cone, right circular, mensuration, 1-18
Conference rooms, see Rooms, conference
Confusion, width of, 20-04
Conical antennas, input impedance, 6-66
Connectors in sound insulation, 12-60, 12-61
Consonants of speech, 12-20
Constaloy, properties, 2-05
Constant (constants), abbreviation, 1-71
arbitrary, 1-13
attenuation, symbol, 1-72
current modulation, 7-74
dielectric, abbreviation, 1-73
frequency oscillator, 7-87
image transfer, 5-13
INDEX
11
Constant (constants), of integration, 1-13
physical, 1-79
time, symbol, 1-73
vibration, symbol, 1-73
-voltage generator, 4-07
wavelength, symbol, 1-73
Constantan, properties, 2-05
Contact potential, 4-10
rectifier, 11-17
Contactors, ignitron, 21-11
thyratron, 21-11
Continental Code, 18-03
Continuity equation, 5-50
Continuous waves, 9-02
Contours of loudness, 12-15
Contrast, roentgenographic, 23-14
television, 20-03
Control electrode, 4-04
grid, 4-04
-grid plate transconductance, 4-06
noise, 10-82
Conversation, power of, 12-22
Conversion factors, 1-42
gain, 11-53
tables, 1-47
angular acceleration, 1-53
angular velocity, 1-53
area, 1-48
capacitance, 1-62
charge per unit area and electric flux density,
1-59
current density, 1-59
density or mass per unit volume, 1-55
electric conductivity, 1-62
electric current, 1-59
electric field intensity and potential gradient,
1-60
electric potential and electromotive force,
1-60
electric resistance, 1-61
electric resistivity, 1-61
energy, work, and heat, 1-57
force, 1-55
inductance, 1-63
length, 1-47
light, 1-65
linear accleration, 1-53
linear velocity, 1-52
magnetic field intensity, potential gradient,
and magnetizing force, 1-64
magnetic flux, 1-62
density, 1-62
magnetic potential and magnetomotive force,
1-64
mass and weight, 1-54
plane angle, 1-51
power or rate of doing work, 1-58
pressure or force per unit area, 1-56
quantity of electricity and dielectric flux,
1-58
solid angle, 1-51
specific heat, 1-64
thermal conductivity and resistivity, 1-65
time, 1-51
torque or movement of force, 1-56
volume, 1-49
transconductance, 4-22
defined, 4-06
Coordination, induction, 10-73
structural, 10-68
Copaline, 2-36
Copel, properties, 2-05
Copper chloride, properties, 2-10
-clad steel wire, 2-20
Copper-iron, properties, 2-05
-manganese, properties, 2-05
-manganese-iron, properties, 2-05
-manganese-nickel, properties, 2-05
oxide, properties, 2-10
plates, 1-68
properties, 2-03, 2-10
sheets, 1-68
standard, 2-02
temperature coefficients, 2-03
wire (tables), 2-12, 2-13, 2-14, 2-15, 2-16
Cord, abbreviation, 1-71
of wood, conversion factors, 1-49
Cordierite, 2-36
ceramic, properties, 2-26
Core loss, 2-59
of power transformers, 6-28, 6-29
resistance, measurements of, audio-frequency
transformer, 6-25
materials for pulse applications, 9-28
Corkboard, compliance and resistance data in in-
sulation of vibration, 12-62
Co-ro-lite, 2-36
Corona, 2-54
Corprene, 2-36
Corronil, properties, 2-05
Cos, 1-07, 1-21
Cosecant, 1-07
abbreviation, 1-71
antennas, 6-72, 6-87
hyperbolic, 1-10
Cosh, 1-10, 1-26
Cosine, 1-07
abbreviation, 1-71
hyperbolic, 1-10
abbreviation, 1-71
Cot, 1-07
Cotangent, 1-07
abbreviation, 1-71
hyperbolic, 1-10
Coth, 1-10, 1-26
Cottonseed oil, relation between dielectric con-
stant and resistivity, 2-51
Coulombs, 1-44, 1-45, 1-46
absolute, 1-43 fn
conversion factors, 1-58, 1-59
Coulomb's law, 1-46
Counter electromotive force, abbreviation, 1-71
Counterpoise, 6-69, 6-80
graphical symbol, 1-76
Counters, frequency, 9-13
Coupled circuits, 6-02, 6-06
audio-frequency transformers, 6-13
common impedance in, 6-06
complex coupling, 6-07
currents, 6-07
mutual impedance, 6-06
overall selectivity curve, 6-10
pure coupling, 6-07
resonant, staggered tuning, 6-10
selectivity, 6-10
self-reactances, 6-07
self-resistances, 6-07
transmission-frequency characteristic, 6-09
voltages, 6-07
Couplet, unidirectional, 6-73
Coupling factor, 6-07
time constant of pulse amplifiers, 9-14
units, flexible, 10-18
Couplings, adequate, 6-09
capacitance, 6-07
coeflicients, 6-09, 6-10
symbol, 1-72
combined self and mutual inductance, 6-07
12
INDEX
Couplings, compound, tuned r-f transformer em-
ploying, 6-11
critical, 6-08
denned, 6-08
selectivity, 6-10
decrement coefficients, 6-09
deficient, 6-09
degrees, 6-09
effect of leakage reactance, 6-11
inadequate, 6-09
inductance, 6-07
loop, graphical symbol, 1-77
output, 4-47
mutual inductance, 6-07
output, magnetrons, 4-47
reactance, 6-07, 6-08, 6-09
resistance, 6-07, 6-08, 6-09
selectivity of i-f amplifiers and, 7-59
sub, 6-09
sufficient, 6-09
super, 6-09
types, 6-07
wave-guide output, 4-47, 4-48
Course sharpness, denned, 22-05
Court rooms, acoustic design, 12-41
Coverage, police radio, 16-37
Critical angle, 5-54
coupling, 6-08
defined, 6-08
selectivity, 6-10
grid potential, 4-59
voltage, 4-40, 4-59
Cronin, properties, 2-05
Cronit, properties, 2-05
Crookes tube, 4-58
Crosby method of frequency control, 8-13
Cross arm, 10-55
lime, 11-41
modulation, 4-24
Crossbar telephone system, 17-26
crossbar switch, 17-26
marker, 17-26
multi contact relay, 17-28
operation, 17-29
Crosstalk, far-end, 11-38
interference, in f-m systems, 8-29
measurement, 11-37
near-end, 11-38
Crystal detector, 7-76
graphical symbol, 1-76
receivers, 7-117
oscillators, 7-92
Crystals, axes, 13-56
ferroelectric, 13-57
microphone, 13-25
piezoelectric, see Piezoelectric crystals
Csc, 1-08
Csch, 1-10, 1-26
Cubic, abbreviation, 1-71
centimeter, abbreviation, 1-71
conversion table, 1-49
equations, 1-03
feet, conversion table, 1-49, 1-50
per minute, abbreviation, 1-71
foot, abbreviation, 1-71
inch, abbreviation, 1-71
conversion table, 1-49, 1-50
measure, 1-49
meter, abbreviation, 1-71
conversion table, 1-49
yard, abbreviation, 1-71
conversion table, 1-49
Cumene, dielectric properties, 2-49
Cunico, 2-67, 2-68
Cunife, 2-67, 2-68
Cupron, properties, 2-05
Cuprous oxide cell, 15-13
Curie point, 2-70
Current (currents), anode, defined, 4-05
cathode, denned, 4-05
density, cgs unit, 1-46
conversion table, 1-59
mks unit, 1-46
symbol, 1-46, 1-72
electric, cgs unit, 1-461
conversion table, 1-59
mks unit, 1-46
symbol, 1-46
filament, 4-08
defined, 4-05
gas, defined, 4-05
grid, defined, 4-05
heater, 4-08
defined, 4-05
in coupled circuits, 6-07
ionization, 4-10
leakage, 4-10
defined, 4-05
loops, 5-26
maximum secondary, conditions for and value;
of, in two mesh circuits, 6-09
measurement, 11-16
nodes, 5-26
non-sinusoidal, 5-02
of antennas, 6-66
plate, denned, 4-05
space-charge limited, 4-02
symbol, 1-72
temperature limited, 4-02
transferred reactance, 6-08
transferred resistance, 6-08
Curtis winding, 11-19
Curve (curves), common, equations, 1-05
demagnetization, 2-59
of permanent-magnet materials, 2-65
grid characteristic, 4-10
magnetization, 2-68
permeability, 2-57
universal resonance, 6-04
Cutoff frequencies, of filters, 6-33
of networks, 6-38
parabola, 4-40
voltage, 4-40
formula, 4-40
Cycles per second, abbreviation, 1-71
Cyclohexane, dielectric properties, 2-49
Cycloid, mensuration, 1-17
Cyclotron, 23-17
frequency magnetrons, 4-41
Cylinder, right circular, mensuration, 1-18
Cylindrical optics of antennas, 6-77, 6-86
Cymbals, power of, 12-25
Cymene, dielectric properties, 2-49
Damped impedance, 5-65
wave transmitter, 7-94
Damping constant or coefficient, symbol, 1-72
constants of sounds, 12-20
Davisson coordinates, 4-09
Days, conversion table, 1-51
db, 1-38
dbm, 1-41
dby, 1-38
D-c amplifiers, 21-16
and low-frequency line testing, 11-41
component, television, 20-03
control power supplies, stabili/ed, 21-14
reinsertion, 9-17, 20-16
INDEX
13
D-c telegraph system, 18-18
Dead-end filter, 5-32
Deafness, 12-07
visible hearing and, 12-21
visual telephony and, 12-21
Decade resistance boxes, 3-20
standard, 11-20
Decahydronaphthalene, dielectric properties, 2-49
Decane, dielectric properties, 2-49
Decay of sound, 12-42
curves, 12-46
Decibels, 1-37
abbreviation, 1-71
Decigrams, conversion factors, 1-54
Deciliter, conversion factors, 1-49
Decimal Gage, 1-66
Decimales, bougie, conversion factors, 1-65
Decimeters, conversion factors, 1-47
Decimetric waves, 1-80
Decineper, 1-37
Decrement, 6-04
Decylene, dielectric properties, 2-49
De-emphasis low-pass filter, f-m receivers and,
8-31
Deficient coupling, 6-09
Definition, television, 20-02
Deflection, 20-08
electrostatic, 20-08
output amplifier, 20-61
magnetic, 20-10
output amplifier, 20-61
sensitivity, 15-42
Degree, abbreviation, 1-71
Centigrade, abbreviation, 1-71
conversion table, 1-51
Fahrenheit, abbreviation, 1-71
Kelvin, abbreviation, 1-71
of freedom, 5-56
Reaumur, abbreviation, 1-71
Deionization time of gas-filled oscillators, 7-91
Dekagram, conversion factors, 1-54
Dekaliter, conversion factors, 1-49
Dekameter, conversion factors, 1-47
Delay, 5-36
characteristics in f-rn distortion, 8-26
defined, 5-36
distortion, 5-16
envelope, 5-36
intercept, 5-36
lines for pulse circuits, 9-28
phase, 5-36
sound, 12-70
Delta function, 5-27
Demagnetization curve, 2-59
of permanent-magnet materials, 2-65
Demagnetizing factor, 2-73
Demodulation, defined, 7-76
Density, cgs unit, 1-46
charge, abbreviation, 1-72
conductors, 2-04
conversion table, 1-55
current, symbol, 1-72
energy, cgs unit, 1-46
mks unit, 1-46
symbol, 1-46
flux, magnetic, cgs unit, 1-46
conversion table, 1-63
mks unit, 1-46
symbol, 1-46
mks unit, 1-46
roentgenographic, 23-14
symbol, 1-46
Deposited-carbon resistors, 3-15
Depth, localization, 12-18
Depth, perception of, 14-45
Derivatives, 1-12
Design, building, calculation of insulation, 12-69
transformers, 6-22, 6-23, 6-28, 6-31
Destruction of tissue, 23-12
Detection, crystals and, 7-80
denned, 7-76
distortion-free, 7-81
linear, 7-79
detection mutual conductance, 7-81
detection plate resistance, 7-81
transrectification factor, 7-81
rectification diagrams of detecting device, 7-79
square-law, 7-76, 7-78
detector circuits, 7-78
static characteristic of diode, 7-77
static characteristic of iron contact on ferro-
silicon, 7-77
static characteristic of triode, 7-77
vacuum tubes and, 7-80
Detectors, 7-76, 11-31
crystal, graphical symbol, 1-76
devices serving as, 7-76
diode, 7-79
distortion and, 7-80
frequency, see Frequency detectors
grid current, 7-79
ideal characteristic, 7-80
load rectification diagram for diode, 7-81
peak, 7-79
plate current, resistance coupled to succeeding
amplifier tube, 7-78
pulse, 9-24, 9-26
sensitivity, denned, 11-50
square-law, detection of carriers and, 7-76
single sideband signals and, 7-76
tetrode, 7-82
load rectification diagrams, 7-82
load rectification of, 7-82
Determinants, 1-04
Deviation ratio of frequency modulation, 8-03
Devices, electro-optical, 15-02
photoresponsive, see Photoresponsive devices
thermal, see Photoresponsive devices, thermal;
Thermal devices
DF stations, 22-04
Diamagnetic materials, 2-57
Diameter, abbreviation, 1-71
Diaphragms, 13-08
cone, 13-09
curvilinear, 13-09
elliptical, 13-09
Diathermy, apparatus, 23-04
technique, 23-06
Diatonic scale, 11-09
Dichlorodifluoromethane, 2-56
Dielectric absorption, in liquids, 2-51
in solids, 2-23
coefficient for free space, cgs unit, 1-46
mks unit, 1-46
symbol, 1-46
constant, of gases, 2-53
of insulating material, 2-21
of liquids, 2-48
of solids, 2-29
symbol, 1-73
flux, conversion table, 1-58
lenses, use in antennas, 6-78
losses, 4-18
materials, solid, 2-25 .
properties, of insulating materials, 2-21
strength, of gases, 2-54
of liquids, 2-51
of solids, 2-23
14
INDEX
Dielectrics, gases as, 2-53
liquid, 2-48
Difference limen of hearing, 12-09
of potential, 1-73
Differential equations, 1-13]
operator, 5-29
sensitivity of hearing, 12-09
Differentiation of pulse in pulse shaping circuits,
9-15
Diffraction, 10-32
Dilectene, 2-34, 2-36
Dilecto, 2-36
Dilver, properties, 2-05]
Diode, 4-02
defined, 4-04
detector, 7-79
gas-filled, 4-02
graphical symbol, 1-77
load impedance, ratio of alternating-current to
direct-current in i-f amplifiers, 7-59
pentode tube of superheterodyne receiver, 7-121
Diplexing of picture and sound, 20-67
Diplopia, 14-28
Dipole, 6-62
Direct capacitance, 11-24
current, abbreviation, 1-71
frequency modulation, 8-12
frequency control of, 8-13
radiator speaker, 13-11
resistance coupled amplifiers, 7-04
Direction finders, airborne, 22-05
automatic, 22-04
finding, 22-04
_ of antennas, 6-87
of rotation (trigonometric), 1-06
Directional baffle, 13-11
characteristics of long wires in antennas, 6-74
couplers, 11-73
diagrams of horizontal and vertical half-wave
antennas, 6-75
Directivity, of hearing, 12-07
of linear conductor antennas, 6-73
of quasi-optical antennas, 6-76
of quasi-optical horns, 6-76
principle of, antennas and, 6-71
Discrete frequency analysis, 11-59
Discrimination ratio, 7-115
Discriminators as frequency detectors, 8-19
Dispersion-hardening alloys, 2-66
Displacement, electrical, cgs unit, 1-46
mks unit, 1-46
symbol, 1-46, 1-73
Display devices, 20-08
Dissector, image, see Image dissector
Dissipation factor, 2-22
Distance measurement, 9-09
reflection of pulse, 9-10
return of pulse, 9-10
-measuring equipment, 22-05, 22-20
range, defined, 22-06
viewing, 20-02
Distortion, 5-16, 14-12
amplitude, 5-33
correctors in passive circuits, 6-05
delay, 5-16
effects on speech and music, 12-29
-free detection, 7-81
frequency, 5-16
effect on sounds, 12-30
modulation, see F-m distortion
in driver transformer, 6-22
in f-m systems, 8-26
intermodulation, measurement, 11-33
introduced by r-f amplifier tubes, 4-24
Distortion, linear passive networks, 5-16
modulation, 4-24
non-linear, 5-38
effects on articulation, 12-34
phase, 5-33, 20-05
audible effects, 12-37
second harmonic, 4-24
telegraphy, 18-11
teletypewriter, 18-15
third harmonic, 4-24
Distortionless lines, 5-26
Distributed capacitance, 3-03, 3-32, 6-14
Diurnal characteristic, 10-39, 10-41
Diverse waves in distance observation, 9-09
Diversity reception of Musa receiving antenna,
6-83
Dividers, frequency, 9-13
Dodecane, dielectric properties, 2-49
Doherty amplifier, 7-131, 7-132
Domains, magnetic, 2-68
Doors, coefficients of sound transmission, 12-65
noise-reduction factor and, 12-69
Dosage, x-ray, 23-13
Dot sequential television, 20-65
Dozen, abbreviation, 1-71
Double-pulse generator, 9-24
-tuned circuits of amplifiers, 7-64
-tuned transformers, three cascade, f-m distor-
tion from, 8-27
two cascade, amplitude characteristic, 8-28
vibration, 11-02
Doublet, 5-52, 6-63
Downward amplitude modulation, f-m distortion
and, 8-29
Drachm, conversion factors, 1-50, 1-54, 1-55
Dram, abbreviation, 1-71
Dri-film, 2-36, 2-45
Drift space, 4-51
Drive-in theaters, 16-25
Driver circuits, 7-22
Driver transformers, 6-22
distortion, 6-22
frequency response, 6-22
leakage reactance, 6-22
turns ratio, 6-22
winding arrangement of class B, 6-22
Driving point admittance, 5-07
impedance, 5-06, 5-10
Drum, power of, 12-25
Dry measure, conversion factors, 1-50
Duality, principle, 5-07
Ductile alloys, 2-68
Dumet, properties, 2-05
Dummy antenna loads, 3-22
Durez, 2-36
Durite, 2-36
DV (double vibration), 11-02
Dynamic plate resistance, 5-45
speaker, 13-11
transfer characteristic, 7-15
Dynatron oscillator, 7-89
Dyne, 1-46
Dyne-centimeters, conversion factors, 1-56
Dynes, conversion factors, 1-55
Dynode, graphical symbol, 1-77
E layer, 10-38
€ (base of natural logs), 1-19
Ear, acoustic impedance, 12-04, 12-05
as viewed through aperture of receiver cap,
12-05
artificial, 12-04
auditory nerves, see Auditory nerves
auditory ossicles, 12-02
INDEX
15
Ear, canal, 12-02
cochlea, 12-02
description, 12-02
differential sensitivity and, 12-09
eustachian tube, 12-02
inner, 12-03
helicotrema, 12-03
semicircular canals, 12-03
stapes attached to, 12-02
stirrup, 12-02
left, semi-schematic section, 12-02
middle, 12-02
hammer, 12-02
malleus, 12-02
natural frequency and damping constant, 12-04
outer, 12-02
oval window, 12-02
pinna, 12-02
round window, 12-02
semicircular canal, 12-02
sensitivity, 12-05, 12-06
auditory range, 12-09
auditory sensation area, 12-09
classes of determinations, 12-05
difference between better ear and average of
both ears, 12-06
difference limen and, 12-09
frequency difference limen and, 12-10
intensity difference limen and, 12-10
minimum audible field, 12-05
minimum audible pressure, 12-05
monaural minimum pressure, 12-07
population and, 12-06
possible lower limits, 12-06
pressure levels and, 12-05
sound intensity and, 12-05
stimulation density of auditory nerve endings
and, 12-12
thermal-acoustic noise and, 12-06
threshold of feeling, 12-09
threshold of hearing, 12-05
zero hearing loss, 12-07
Eardrum, 12-02
malleus attached to, 12-02
Earphones, see Telephone receivers
Earth resistivity, effect of, 10-89
Ebonite, 2-36
EC, 2-37
Echelette grating, 11-13
Echo, 12-40, 12-70
flutter, 12-40
in auditoriums, 12-70
multiple, 12-40
testing of lines, 11-38
Eddy-current loss, 2-59
Edison Wire Gage, 1-69
Effective area of non-dissipative antennas, 6-76
conductivity, defined, 2-02
height, 6-70
inductance, 3-03
plate resistance, 5-45
resistance, measurement, 11-27
spot width, 20-04
values, 1-74
Efficiency, abbreviation, 1-71
of audio-frequency transformers, 6-16
of output transformers, 6-18
plate, 7-09
symbol, 1-73
Einthoven galvanometer, 23-09
Elastance, symbol, 1-73
Elastivity, symbol, 1-73
Electric, abbreviation, 1-71
charge, symbol, 1-72
Electric, circuits, see Circuits
conductance, 1-61
conductivity, 1-62
displacement, symbol, 1-73
doublet, 5-52
field intensity, cgs unit, 1-46
conversion table, 1-60
mks unit, 1-46
symbol, 1-46
flux, cgs unit, 1-46
density, conversion table, 1-59
rnks unit, 1-46
symbol, 1-46
induction, 10-73
intensity, symbol, 1-73
moment, symbol, 1-73
polarization, symbol, 1-73
potential, conversion table, 1-60
resistance, 1-61
resistivity, 1-61
units, 1-43
practical, 1-44
wave filters, see Wave filters
Electrical conductance, 1-61
equivalent of heat, 1-79
quantities, measurement, 11-16
systems, 5-56
comparison with mechanical, 5-59
energy, 5-57
units, 1-43
Electricity, medical applications, 23-02
quantity of, symbol, 1-73
Electris, properties, 2-05
Electroacoustic devices, aids to the deaf, 23-11
equipment, 16-11
amplifiers, 16-14
control equipment, 16-14
transducer, 13-02
Electrocardiography, apparatus, 23-08
Electrochemical cauterization, 23-03
Electrode admittance, defined, 4-05
capacitance, defined, 4-06
measurement circuit, 4-14
characteristic, defined, 4-06
conductance, defined, 4-05
deflecting, reflecting or repelling, grapnical
symbol, 1-77
impedance, defined, 4-05
resistance, 4-11
defined, 4-05
Electrodes, conductance, 4-11
control, defined, 4-04
Electrodynamic speaker, 13-11
Electroencephalography, apparatus, 23-08
Electrolysis, 10-63
Electrolytic capacitors, 3-68
Electromagnetic coupling, 5-64
horn (antenna), 6-79
radiation, 5-49
fields due to a current in a wave, 5-52
Maxwell's equations, 5-50
progressive plane waves, 5-51
reflection, 5-52
refraction, 5-52
Electromechanical-acoustic devices, 13-02
-acoustic systems, 5-62
analogues, 5-60, 5-63
frequency control, 8-14
oscillators, 7-91
systems, 5-56, 5-64
electrostatically coupled, 5-62
interaction factors, 5-65
magnetically coupled, 5-64
stabilization, 21-32
16
INDEX
Electromotive force, abbreviation, 1-71
cgs unit, 1-46
conversion table, 1-60
measurement, 3-02
mks unit, 1-46
physiological, 23-08
symbol, 1-46, 1-73
unit, 1-44
Electron currents, stray, 4-11
emission, 4-10
defined, 4-04
gun, 15-41
operation, 15-42
mass of, 1-79
microscope, 23-16
optical systems, general theorems on, 14-63
optics, 14-49
prisms, 14-62
transit angle, 4-53
tubes, Section 4; see also Gaseous conduction
tubes; Klystrons; Magnetrons; Vacuum
tubes ; X-ray tubes
Electronic charge, 1-79
symbol, 1-73
control equipment, 21-02
controls, d-c motor, 21-27
process instrumentation, 21-32
resistance-welder, 21-23
side-register positioning, 21-30
devices, 21-20
numerical integrator and computer (eniac),
9-08
relays, contact-operated, 21-20
tuning, 4-55
sink margin, 4-56
Electrons, mass, 4-14
transit time, 4-15
velocity, 4-14
Electro-optical devices, 15-02
Electrose, properties, 2-26
Electrostatic coupling, 5-62
deflection, output amplifiers, 20-61
scanning circuits, 20-08
lenses, 14-51
system of units, 1-43
Electrosurgery, 23-06
Electrotherapy, apparatus, 23-02
electrochemical cauterization, 23-03
galvanic current, 23-03
iontophoresis, 23-03
kataphoresis, 23-03
miscellaneous, 23-03
Elinvar, properties, 2-05
Ellipse, equation, 1-05
mensuration, 1-18
Ellipsoid, mensuration, 1-18
Elliptical cylinder cavity resonators, 7-101
Emergency transmitters, frequency modulation,
8-15
phase modulators used for, 8-15
Emission characteristic, 4-09
defined, 4-05
Emissions, electron, 4-10
grid, 4-11
Empire, 2-36
Enamel, 2-36
varnish, 2-36
vitreous, 2-36
properties, 2-26
wire, 2-36
End-fire array antennas, 6-72
Energy, cgs unit, 1-46
conversion table, 1-57
density, cgs unit, 1-46
Energy, density, mks unit, 1-46
symbol, 1-46
dissipation, resistors, 3-03
efficiency of speaker, 13-10
integral, 5-35
mks unit, 1-46
of mechanical and electrical systems, 5-57
symbol, 1-46, 1-73
volume, cgs unit, 1-46
mks unit, 1-46
symbol, 1-46
Engineering terms, abbreviations, 1-71
English candles, conversion factors, 1-65
Legal Standard Wire Gage, 1-69
system of units, 1-42
Envelope delay, 5-36
in f-rn distortion, 8-26
double-cavity resonator, graphical symbol, 1-77
gas-filled, graphical symbol, 1-77
high-vacuum, 1-77
shield within, graphical symbol, 1-78
single-cavity resonator, graphical symbol,
1-78
Epstein test, 2-75
Equalizers, attenuation, 16-28
in passive circuits, 6-05
loss, 5-16, 5-18
phase, 5-16, 5-21
Equalizing pulses, 20-13, 20-17
Equally tempered scale, 11-09
Equation, abbreviation, 1-71
algebraic, 1-02
Bessel's, 1-15
calculus, 1-12
circuit, 5-05
common curves, 1-05
containing complex quantities, 1-07
cubic, 1-03
differential, 1-13
exponential, 1-10
hyperbolic, 1-10
Maxwell, 1-45, 5-50
mesh, 5-05
nodal, 5-06
of common curves, 1-05
quadratic, 1-03
simultaneous, 1-03
linear, 1-04
trigonometric, 1-07
wave, 5-51
Equilateral hyperbola, equation, 1-05
Equipment, telegraph, see Telegraph equipment
Equipotential cathode, 4-04
Equivalent circuit, of crystal oscillator circuit,
7-93
of simple antenna, 6-67
of triode, 6-08
impedance, 6-08
negative resistance, 5-49
network, complete, audio-frequency trans-
former of, 6-14
-noise resistances, 4-21
primary impedance, 6-08
quadripoles, 5-13
Ergodic state of acoustics of rooms, 12-41
Ergs, 1-44, 1-46
conversion factors, 1-57, 1-58
Errors of observation, 1-15
Erythema, 23-07
Ethocel, 2-37
Ethofoil, 2-37
Ethyl abietate, dielectric properties, 2-49
acetate, dielectric properties, 2-49
alcohol, dielectric properties, 2-49
INDEX
17
Ethyl alcohol, relation between dielectric constant
and resistivity, 2-51
benzene, dielectric properties, 2-49
cellulose, 2-37
power factor at high frequencies, 2-34
properties, 2-26
ether, dielectric properties, 2-49
Ethylene, dielectric constant, 2-54
glycol, dielectric properties, 2-49
Eureka, properties, 2-05
Eustachian tube of ear, 12-02
Evanohm, properties, 2-05
Excello, properties, 2-05
Excelsior, properties, 2-05
Exchange telephone plant, 17-78
cables, 17-93
design, 17-92
effective transmission performance, 17-79
Icop losses, 17-80
open- wire facilities, 17-96
service requirements, 17-78
Exciter lamp, 16-22
Excitor, graphical symbol, 1-77
Excitrons, 4-80
defined, 4-75
Exhaust fan noise, 11-64
Exponential formulas, 1-10
function of x, 1-10
horn, 13-05
tables, 1-26
wave form, repetition rate of pulses determined
by, 9-19
Exposure meter, photographic, 15-18
External, abbreviation, 1-71
Extrapolation, 4-09
Eyes, aberrations, 14-29
depth of focus, 14-30
movement, 14-28
optical characteristics, 14-29
refractive errors, 14-30
refractive media, 14-26
resolving power, 14-40
retinal rivalry, 14-48
schematic, 14-28
structure, 14-25
visual acuity, 14-40
F layer, 10-38
Facsimile, 18-38, 19-02
duplicators, 19-23
picture elements in, 19-02
reception of, 19-02
recorder, phasing, 19-21
recording amplifiers, 19-16
recording systems, 19-11
carbon-paper, 19-15
comparison, 19-16
dry electrolytic, 19-13
photographic, 19-11
wet electrolytic, 19-12
scanner amplifiers, 19-07
frequency spectrum, 19-07
types, 19-08
typos of signals, 19-08
scanning systems, 19-02
methods used in, 19-03
synchronization, 19-18
magnetic brake, 19-19
start-stop, 19-20
tape systems, 19-23
transmission of, 19-02
radio, 19-22
wire line, 19-22
Factories, noise levels acceptable in, 12-58
Factors, conversion, 1-47
Factory broadcast system, 16-16]
Fading, 10-45
reduction of, 7-125, 18-57
Fahy penneameter, 2-74
Farad, 1-44, 1-45, 1-46
abbreviation, 1-71
conversion factors, 1-62
Faraday constant, 1-79
dark space, 4-59
Faradays, conversion factors, 1-58
Faraday's law, 5-50
Fahrenheit units, 1-43
conversion table, 1-64
Fathom, 1-47
Fault location, 11-41
FCC Standards, television, 20-20
wave form, television, 20-17
Feedback, negative, 7-31, 7-51
of reverberation, 12-47
Feeling, threshold of, 12-09
Feet, see also Foot
conversion table, 1^7
cubic, conversion table, 1-49, 1-50
square, conversion table, 1-48
Felt, hair, 12-63
Fermat's principle, 14-02
Ferroelectric crystals, 13-57
defined, 13-57
Ferromagnetic materials, 2-57
Ferro-nickel, properties, 2-05, 2-10
Ferrous-cored inductor, 3-42
Ferry-Porter law, 14-35
Fiber boards, coefficients of sound transmission,
12-65
bone, properties, 2-26
commercial, properties, 2-26
vulcanized, 2-37
Fiberglas, 2-37
Fibestos, 2-36, 2-37
Fibron, 2-37
Fidelity, determination of, in superheterodyne
receivers, 7-56
Field, 20-06
frequency, 20-20
intensity, 6-70, 10-31
of view, 20-02
sequential television, 20-65
Fields, due to a current in a wire, 5-52
Fifth, 11-08
Figure of merit, 3-31
Filament, defined, 4-04
current, 4-08
denned, 4-05
power, 7-106
transformer, 6-26
voltage, changes in, 4-26
denned, 4-05
Filamentary cathode, 4-08
Filters, see also Wave filters
attenuating band of, 6-33
B supply, 7-108
band-pass, 6-33, 6-58
attenuation (Tchebycheff type) character-
istic, 6-58
illustrative design, 6-59
constant-.^ section, 6-48
cutoff frequencies and, 6-33
design, Tchebycheff type characteristics, 6-56
elementary symmetrical band-pass sections,
6-44, 6-45, 6-46, 6-47
frequency control factors required for specified
reflection coefficient, 6-57
general composite, 6-40
18
INDEX
Filters, general composite, elementary constitu-
ents, 6-49
high-pass, 6-33, 6-58
constant-J£ type image impedance, 6-50
idealized, 5-35
image impedance of general composite, 6-49
image impedance (Tchebycheff type) character-
istic, 6-58
image impedance theorem, 6-39
insertion loas for frequencies, 6-33
low-pass, 6-33, 6-58
constant-J? type image impedance, 6-50
m-derived sections, 6-48, 6-50
TO-derived terminating sections, 6-54
design information for, 6-52
open-circuit transfer impedance, 6-38
pass band of, 6-33
image impedance and, 6-36
simple section, mid-series constant-^ imped-
ance, 6-51
mid-shunt constant- K impedance, 6-51
slope, 8-19
symmetrical, 6-41
high-pass sections, 6-43
image transfer function, 6-56
lattice configuration, 6-41
low-pass sections, 6-43
symmetrical sections, 6-39, 6-41
elementary structures, 6-48
lattice, 6-41
terminating sections having two-image con-
trolling frequencies, 6-54, 6-55
transfer constant theorem, 6-39
two-frequency control image impedance of un-
syrnmetrical sections, 6-53
two-frequency control sections, 6-53
types, 6-33
unsymmetrical sections, 6-50
x-ray, 23-12
First aid, 23-17
Fish paper, 2-37
Fisher-Hinnen method of analysis, 5-47
Fixed capacitance condensers, 3-60
Flamenol, 2-37, 2-48
Flashover, 2-24
Flat field, 20-04
selectivity curve, f-m distortion and, 8-28
-top antennas, 6-62, 6-80
-type resistors, 3-09
Flax-Ii-num, compliance and resistance data in
insulation of vibration, 12-62
Flexible coupling units, 10-18
cushions in sound insulation, 12-60, 12-61
panels, 12-62
resistors, 3-09
wave guides, 10-18
Flexural strength, 2-28
effect, 4-20
Flicker, 20-05, 20-66
requirements, 20-06
Flip-flop circuits, of counters and computers, 9-13,
9-14
stable in either condition, illustrated, 9-17
Floor partitions, 12-66
Fluctuation current, 4-20
noise interference, divisional noise of vacuum
tubes, 8-30
in f-m systems, 8-30
shot noise of vacuum tubes, 8-30
thermal noise, 8-30
voltage, 4-21
Fluid ounce, conversion factors, 1-49, 1-50
Fluorescence, denned, 15-30
Fluorescent lamps, 15-37
Fluoroscopy, tubes, 4-89
Fluor s, denned, 15-30
Flute, power of, 12-25
Flutter echo, 12-40
Flutters, acoustic properties of rooms and, 12-40
Flux density, electric, cgs unit, 1-46
mks unit, 1-46
symbol, 1-46
magnetic, cgs unit, 1-46
conversion table, 1-63
mks unit, 1-46
symbol, 1-46, 1-73
of power transformers, 6-28
dielectric, conversion table, 1-58
displacement f., symbol, 1-73
electric, cgs unit, 1-46
mks unit, 1-46
symbol, 1-46
-linkage, symbol, 1-73
-magnetic, cgs unit, 1-46
conversion table, 1-63
denned, 2-60
mks unit, 1-46
symbol, 1-46
voltmeter, 2-76
F-m distortion, a-m rejection and, 8-29
amplitude modulation, 8-26
balanced discriminator and, 8-28
commercial entertainment receivers and, 8-27
delay characteristics, 8-26
downward amplitude modulation and, 8-29
due to incomplete rejection of amplitude
modulation, 8-27
due to multipath reception, 8-29
envelope delay in, 8-26
flat selectivity curve and, 8-28
f-m detector input-output characteristic, 8-28
from amplitude modulation, 8-28
from three cascade double-tuned trans-
formers, 8-27
harmonic distortion, 8-28
in f-m systems, 8-26
inadequate bandwidth, 8-26
incomplete rejection, 8-26
input capacity of amplifier tubes and, 8-32
modified analysis, method for evaluating,
8-27
multipath distortion effects, 8-29
multipath transmission, 8-26
non-linear phase characteristic, 8-26
non-uniform delay and, 8-26
null in transmission and, 8-29
quasi-steady-state approximation, 8-26
second harmonic, 8-28
side responses, reduction of, 8-29
sideband analysis-synthesis method for eval-
uating, 8-27
skip transmission and, 8-29
small deviation ratio, 8-27
small distortion in systems with, 8-27
third harmonic, 8-28
equipment, measurement of frequency swing,
8-08
receivers, 8-16
a-m receivers and, 8-16
commercial entertainment, f-m distortion
and, 8-27
frequency detectors of, 8-19
limiters, grid-bias, 8-24
multiple tuning positions, 8-17
superheterodyne principle, 8-16
systems, adjacent-channel interference in, 8-30
beatnote and, 8-30
co-channel interference in, 8-30
INDEX
19
F-m. systems, de-emphasis low-pass filter and,
8-31
fluctuation noise interference, 8-30
impulse noise interference in, 8-31, 8-32
carrier amplitude and, 8-32
"click," 8-32
grid-bias limiter and, 8-32
"pop," 8-32
pulse of phase modulation and, 8-32
step of phase modulation and, 8-32
transient impulse amplitude and, 8-32
interference in, 8-26, 8-29
audio noise, rms value of, and, 8-31
fluctuation noise, 8-29
f-m ratio and, 8-31
impulse noise, 8-29
noise signals, 8-29
output noise spectrum and, 8-31
spurious receiver responses, 8-29
large deviation ratio and, 8-31
peak noise, 8-31
signal-to-interference ratio, 8-30
signal-to-noise ratio importance and, 8-31
small deviation ratio and, 8-31
threshold for f-m improvement, 8-31
triangular f-m beatnote spectrum and, 8-30
transmitters, 8-09
circuits, 8-15
for emergency communication, 8-09
for f-m broadcasting, 8-09
sound transmitters for television broadcast-
ing, 8-09
types, 8-09
Focusing of sound, 12-70
Foot, see also Feet
abbreviation, 1-71
-candle, abbreviation, 1-71
cubic, abbreviation, 1-71
-Lambert, abbreviation, 1-71
-pound, abbreviation, 1-71
conversion factors, 1-57, 1-58
-second (system), abbreviation, 1-71
square, abbreviation, 1-72
Force, cgs unit, 1-46
coercive, defined, 2-59
conversion table, 1-55
counter electromotive, abbreviation, 1-71
electromotive, abbreviation, 1-71
measurement, 3-02
symbol, 1-73
unit, 1-44
factor of speaker, 13-12
magnetizing, 2-57
cgs unit, 1-46
conversion table, 1-64
defined, 2-60
mks unit, 1-46
symbol, 1-46
magnetomotive, abbreviation, 1-71
cgs unit, 1-46
conversion table, 1-64
mks unit, 1-46
symbol, 1-46, 1-73
mks unit, 1-46
moment of, conversion table, 1-56
per unit area, conversion table, 1-56
standard of, 1-42
symbol, 1-46, 1-73
Foreign wire relations, 10-67
Formation voltage, 3-69
Formex, 2-37, 2-47
Formica, 2-37
Forming voltage, 3-69
Formulas, algebraic, 1-02
Formulas, approximation, 1-16
calculus, 1-12
cutoff voltage, 4-40
exponential, 1-10
hyperbolic, 1-10
mensuration, 1-17
temperature conversion, 1-64
trigonometric, 1-07
Formvar, 2-37, 2-47
Forticel, 2-36, 2-37
Fortisan, 2-37
Foster's theorem on driving point impedances,
6-35
Fourier integral, 5-27, 5-33
series, 5-27, 5-33
Fourier's theorem, 5-02
Four-terminal networks, 5-10, 6-33
driving point impedances, 5-10
equivalent quadripoles, 5-13
image parameters, 5-13
lattice or bridge, 5-13
restrictions for physical readability, 5-11
T and TT, 5-13
terminated, 5-11
transfer impedance, 5-10
Fourth, 11-08
Frame, 20-06
frequency, 20-20
Free charge, 2-23
Free-running multivibrator, 9-18
space transmission law of antennas, 6-72
Freedom, degrees of, 5-56
Freezing point, abbreviation, 1-71
French horn, power of, 12-25
Freon, 2-56
Frequencies, band, analysis, 11-56
complex, 5-04
defined, 11-02
discrete, distribution, 11-54
extremely high, 1-80
formulas, 11-03
high, 1-80
low, 1-80
measurements, 11-02
medium, 1-80
nomenclature, 1-80
spectrum of electrical phenomena, 11-14
super high, 1-80
ultra high, 1-80
measurement, 11-11
very high, 1-80
very low, 1-80
Frequency allocation, television, 20-20
analysis of exhaust fan noise, 11-64
angular, symbol, 1-73
bandwidth, required for a certain speed of in-
formation, 9-04, 20-04
widening of square pulse by reduction, 9-04
cgs unit, 1-46
characteristics, measurements of, audio-fre-
quency transformer, 6-25
of input and interstage transformers, 6-20
comparison, 11-05
control, see also Frequency modulation
Crosby method, 8-13
direct frequency modulation, 8-13
electromechanical, 8-14
pulse counter, 8-14
counters, 9-13
field, 20-20
flip-flop circuits, 9-13
frame, 20-20
detectors, discriminator characteristics, 8-20
discriminator circuits, 8-20
20
INDEX
Frequency detectors, discriminators as, 8-19
of f-m receivers, 8-19
ratio-type, 8-21
amplitude compensation, 8-23
regulation curves, 8-22
side-tuned circuits as, 8-21
slope filter as, 8-19
simple, 8-19
difference limen, of hearing with decibels above
threshold (hearing), 12-10
discrimination, 11-63
distortion, 5-16
distortion, effects on sounds, 12-30
resonance type, effect on articulation, 12-33,
12-34
dividers, 9-13
counting type, 9-13
division in pulse circuit, 9-13
effect on magnetization, 2-70
meters, induction, 11-11
vibrating-reed, 11-11
Weston, 11-11
mks unit, 1-46
modulation, 7-71, 8-02, see also Frequency con-
trol
Beasel functions, 8-04
values, 8-05
broadcasting, 8-09, 16-31
amplitude noise, 8-10
coverage, 16-32
distortion, 8-10
frequency characteristic, 8-10
frequency control and modulation, 8-10
intermediate frequency, 8-16
noise level, 8-10
transmitter, 8-10
by input capacitance variation, 8-12
by phase-modulation method, 8-11
by reactance tubes, 8-12
degree of, 8-04-
detector, a-m rejection in, 11-53
input-output characteristic, distortion and,
8-28
deviation ratio, 8-03
direct, 8-12
discriminator action of detectors, 8-03, 8-19
distortion, see F-m dintortion
equivalent sideband, 8-04
for emergency transmitters, 8-15
frequency detector conversion, 8-17
frequency swing, 8-04
from non-uniform amplitude and phase char-
acteristics, 8-2(5
fundamental relations, 8-02
mathematical equivalent of discriminator ac-
tion, 8-09
measurements, 11-50
methods, 8-10
modulation index, 8-03, 8-04, 8-05
noise characteristics, 8-31
pass band, transmitting and receiving, and,
8-02
peak angle swing and, 8-06
receivers, see F-m receivers
sideband distribution, 8-06
sidebands and, 8-02
single-, 8-02
studio-transmitter link use of, 8-02
systems, 8-02
theory of noise suppression and, 8-03
transmitters, see F-m transmitters
two-frequency, 8-07
multipliers, 9-13
range, audible, 12-30
Frequency response of output transformers, 6-17
rotational, symbol, 1-73
sensitivity, 12-10
shift, effects of, 12-35
spectrum, 5-28
of pulse, 9-11, 9-12
stability of oscillation, 7-92
standard used in frequency measurement,
11-05
swing of frequency modulation, 8-04
symbol, 1-46, 1-73
Fricative consonants of speech, 12-20
fill in visible speech, 12-21
Frictional modulation in speech, 12-19
Frolich-Kennelly relation, 2-69
Front feed for reflectors of antennas, 6-86
porch, 20-16
-wall effect, 15-13
Frustum, volume of, 1-18
Full coaxial cylinder cavity resonator, 7-98, 7-101
-wave rectifier, 7-107
Fullerboard, 2-37
Furfural resins, 2-37
Furlong, conversion factors, 1-47
Fuse, 17-05
Fusion point, abbreviation, 1-71
G. E. Mycalex, 2-38
Gages, 1-66
sheet metal, 1-66
wire, 1-66, 1-68, 1-69, 1-70, 2-12
comparison, 1-09, 1-70
Gain, control, 16-07
insertion, 11-32
Gallium, properties, 2-05
Gallon, abbreviation, 1-71
British Imperial, convcrnion factors, 1-50
liquid, conversion tablo, 1-19
U. S. (dry measure), conversion factors, 1-50
XT. S. (liquid), convorHion factors, 1-50
Galvanized Sheet Gage, 1-66
Galvanometer, graphical symbol , 1-76
Gamma (transfer characteristic), 20-29
correction, 20-29
Gang tuning condenser, 7-121
Gap spacing, 4-53
Gas current, defined, 4-05
-filled oscillators, deionization time of gas in
operation, 7-91
ionization time of gas in operation, 7-91
-filled tubes, 4-02
triodo, 4-59
tube, defined, 4-03
volume, 1-79
x-ray tubes, 4-81
Gaseous conduction, 4-58
tubes, 4-58
Gases, as dielectrics, 2-53
conductivity, 2-54
dielectric strength, 2-54
iomzation, 2-54
Gauss, 1-46
conversion factors, 1-63
Gelva, 2-37
General composite filters, 6-40
elementary constituents, 6-49
filter network, 6-33
-purpose triode, 4-31
Generalized displacement, 5-57
mass, 5-57
velocity, 5-57
Generators, constant voltage, 4-07
double-pulse, 9-24
multiple-pulse, 9-24
INDEX
21
Generators, of constant current, 4-07
Geometrical progression, 1-02
representation of complex number, 1-06
Geon, 2-37, 2-47, 2-48
German candles, conversion factors, 1-65
silver, properties, 2-05
Germanium, properties, 2-05
Gilbert, 1-46
conversion factors, 1-64
Gill, liquid, conversion factors, 1-49, 1-50
Gilsonite, 2-35, 2-37
Giorgi, 1-45
Glass, 2-37
-bonded mica, 2-38
power factor at high frequencies, 2-34
properties, 2-26
high silica, power factor at high frequencies,
2-34
properties, 2-10, 2-26
Pyrex, power factor at high frequencies, 2-34
textiles, 2-38
Glide path, 22-15
Glottis of vocal cords, acoustic wave form pro-
duced at, 12-19, 12-20
Glow-discharge tubes, 4-72
Glowray, properties, 2-05
Glycerin, dielectric properties, 2-49
Glyptal, 2-34T 2-3S
Gold, properties, 2-05, 2-10
Goldschmidt alternators, 7-94
Goniometer, 22-08
Gradient, potential, cgs unit, 1-46
conversion table, 1-60
mks unit, 1-46
symbol, 1-46
Grahamite, 2-35
Grain-oriented materials, 2-61
Grains, conversion factors, 1-54, 1-55
Gram, abbreviation, 1-71
-calorie, 1-65
abbreviation, 1-71
conversion factors, 1-57, 1-64, 1-65
-centimeters, conversion factors, 1-56
conversion factors, 1-54, 1-55
Graphical symbols, 1-76
Graphite grains, properties, 2-10
properties, 2-10
Gravity, acceleration, 1-79
specific, abbreviation, 1-72
Greek alphabet, use for symbols, 1-79
Grenz rays, 23-12
Grid bias, denned, 4-05
-bias Hmiters, 8-24
characteristic curve, 4-10
control, defined, 4-04
current, defined, 4-05
detector, 7-79
defined, 4-04
driving power, defined, 4-05
emission, 4-11
defined, 4-05
graphical symbol, 1-77
leak, 7-93
modulation, 7-73
-plate characteristic, 4-11
-plate transconductance (mutual conductance) ,
5-42
resistance, 4-11
maximum allowable, 4-27
resistors, 3-11
screen, defined, 4-04
space-charge, defined, 4-04
suppressor, defined, 4-04
voltage, defined, 4-05
Grinders, 10-43
Gross ton, conversion factors, 1-54
Ground controlled approach, 22-26
graphical symbol, 1-76
return circuit, 10-87
system, antennas and use of, 6-69
Wagner, 11-26
wave, see Wave propagation, ground wave
wires, 10-93
Grounded capacitors, 11-24
-grid amplifiers, 7-31, 7-49
Group velocity, 5-36
Growth of sound, 12-42
Gullstrand schematic eye, 14-28
Gummon, 2-38
properties, 2-26
Gunther's chain, conversion factors, 1-47
Gutta-percha, 2-38
properties, 2-26
Hair felt, 12-53, 12-56
Half -wave antenna, 6-71
Halowax, 2-38
Hand, conversion factors, 1-47
Hard plaster, 12-55
rubber, 2-38
x-rays, 4-82
Harmonic amplifiers, radio transmitters and,
7-130
analysis, of current for a sinusoidal applied
voltage, 5-46
distortion in f-m systems, S-28
Harmonics, of the intermediate frequency of
superheterodyne receivers, 7-122
Hartley oscillators, 7-93
Heading, defined, 22-05
Heaped bushel, conversion factors, 1-50
Hearing, average loss, 12-08
binaural vs. monaural, 12-06
difference limen, 12-09
limits of, 12-08
mechanism of, 12-02
monaural, 16-02
of speech, effect of noise and, 12-72
effect of reverberation on, 12-73
in auditoriums, 12-69
sense of, 12-02
tests with, losses greater than 25 db and 45 db,
12-09
variation with age, 12-07
Heart disease, diagnosis, 23-09 _
human, relaxation oscillation in, 7-84
sound of, 23-09
Heat, conversion table, 1-57
electrical equivalent, 1-79
mechanical equivalent, 1-79
quantity of, cgs unit, 1-46
mks unit, 1-46
symbol, 1-46
specific, abbreviation, 1-72
conversion table, 1-64
Heater current, 4-08
denned, 4-05
defined, 4-04
delay, 7-114
graphical symbol, 1-77
voltage, changes in, 4-26
denned, 4-05
Heating effect of r-f current, 23-04
of power transformer, 6-29
time, cathode, 4-08
Heaviside layer, 10-37
Lorentz system of units, 1-43
operational calculus, 5-34
INDEX
Heaviside, unit function, 5-27
Hectare, conversion factors, 1-48
Hectogram, conversion factors, 1-54
Hectoliter, conversion factors, 1-49
Hectometer, conversion factors, 1-47
Hectometric waves, 1-80
Hefners, conversion factors, 1-65
Height, effective, 6-70
Heising modulation, 7-74
Helicotrema of ear, 12-03
Helium, minimum sparking potentials, 2-54
Hemispheres, conversion table, 1-51
Hemit, 2-38
properties, 2-26
Henry, 1-44, 1-45, 1-46
abbreviation, 1-71
conversion factors, 1-63
Heptane, dielectric properties, 2-49
Heptode, denned, 4-04
Hercules EC, 2-37
Herculite, 2-38
Heterodyne analyzer, 11-61, 11-66
Heterophoria, 14-29
Heusler alloys, 2-57
Hexane, dielectric properties, 2-49
Hexode, defined, 4-04
High-fidelity broadcasting, 16-33
-frequency antenna, 6-82
-frequency broadcasting, 16-31
compensation methods of wide-band ampli-
fiers, 7-43
surgery, 23-06
apparatus, 23-04
-H per mea meter, 2-74
-inductance antenna coupling of radio receivers,
7-115
level modulation, 7-74
-pass filter, 6-33
-permeability materials, 2-60
-power audio amplifiers, 7-22
-power radio transmitters, 7-136
audio equipment, 7-136
~Q circuits of i-f amplifiers, 7-62
resistances, 3-17
transmission, 10-05
-vacuum tubes, 4-02
defined, 4-04
-voltage shock, 23-17
-voltage therapy tubes, 4-85
Highlight brightness, 20-03
Hinge joints of wave guides, 10-26
Hipernik, properties, 2-06
Hiss tone in speech, 12-21
Hole-and-slot magnetrons, 4-42
Homes, noise levels acceptable in, 12-58
Hopkinson alloy, properties, 2-06
Horizontal hyperbola, 1-05
parabola, 1-05
polarization, 20-20
resolution, 20-04
synchronizing pulse, 20-17
Horizontally polarized antenna, 6-85
Horns, 6-79, 13-05, 13-10
biconical, 6-80
catenoidal, 13-06
conical, 6-80
defined, 13-05
directional properties, 13-08
electromagnetic, 6-79
forms of, 6-80
pyramidal, 6-80
quasi-optical, directivity of, 6-76
Salmon, 13-06
sectoral, 6-80
Horsepower, abbreviation, 1-71
conversion factors, 1-58
-hour, abbreviation, 1-71
conversion factors, 1-57
metric, conversion factors, 1-58
Hospitals, noise levels acceptable in, 12-58
Hot-cathode thyratrons, 4-71
x-ray tubes, 4-81
Hotels, noise levels acceptable in, 12-58
sound insulation, 12-57
Hour, abbreviation, 1-71
conversion table, 1-51
Humidity, variations in, use of stable fixed con-
densers and tuning by iron-core coils, 7-60
Hundred, abbreviation, 1-71
Hundredweight, conversion factors, 1-54
Huygens' principle of wave propagation, 6-76
Hybrid coils, see Transformers, three winding
junctions, 11-75
Hycar, 2-38
OR, 2-35
Hydrogen, acoustic properties, 13-02
dielectric constant, 2-54
dielectric properties, 2-49
minimum sparking potentials, 2-54
Hyperbola, equation, 1-05
Hyperbolic cosine, abbreviation, 1-71
formulas, 1-10
functions, 1-10
chart, 1-26
relations between trigonometric functions
and, 1-11
logarithms, 1-19
radians, 1-26
sine, abbreviation, 1-71
tables, 1-26
tangent, abbreviation, 1-71
Hysteresis loops, 2-58
Hytemco, properties, 2-06
la la, properties, 2-06
Ice load, 10-51
point, 1-79
Iconoscope, 15-21
construction, 15-21
operation, 15-22
resolution, 15-24
sensitivity, 15-24
signal-to-noise ratio, 15-24
studio television camera, 20-23
uniformity, 15-25
Ideal, properties, 2-06
transducer, 5-15
Idealized filters, 5-35
I-f amplifiers, 7-56
as source of gain and selectivity in radio re-
ceiver, 7-58
broad, 7-60
coefficients of coupling, 7-59
critically coupled circuits, 7-59
double-tuned stage, 7-63
flat-topped selectivity curve, 7-59
for a-m broadcast receivers, 7-58
for f-m receivers, 7-61
medium bandwidth, 7-58
narrow bandwidth, 7-58
of superheterodyne receiver, 7-121
opposing couplings, gain, and bandwidth of
i-f stage, 7-60
opposing inductive and capacitive coupling
and, 7-60
pulse technique of, illustrated, 9-14
r-f, 7-129
tuning stability, 7-60
INDEX
23
I-f amplifiers, variable selectivity, 7-59
wide-band, 7-63
gain and bandwidth, 11-53
harmonics, feedback of, 7-61
sensitivity, defined, 11-50
Igniter, defined, 4-75
graphical symbol, 1-77
Ignitrons, 4-78
contactors, 21-11
defined, 4-75
ignitor characteristics, 4-80
rectifiers, 21-10
tests, 4-80
Ilium, properties, 2-06
Illuminance, 14-16
Illumination, cgs unit, 1-46
mks unit, 1-46
symbol, 1-46
visual acuity and, 14-42
Image, characteristics, 15-44
dissector, 15-19
resolution, 15-21
sensitivity of, 15-20
signal-to-noise ratio, 15-21
uniformity of, 15-21
impedances, 5-13, 6-37
characteristics of m^-derived filter sections,
6-53
of general composite filter, 6-49
of two-frequency control sections of filters,
6-53
theorem of filters, 6-39
wave-propagation theory and, 6-33
orthicon, 15-27
resolution, 15-29
sensitivity, 15-29
studio television camera, 20-23
uniformity, 15-29
parameters, 5-13
coincidence conditions, 6-36
properties, 6-36
summary of properties, 6-38
response of superheterodyne receivers, 7-122
transfer constant, 6-33
wave-propagation theory and, 6-33
transfer functions, of networks, 6-37
of symmetrical filter, 6-56
Imaginary period, 1-10
quantity, 1-06
unit, 1-06
Impact sounds of noise conduction, 12-60
Impedance, blocked, 5-65
bridge, in circuits, 6-12
characteristic, 10-02
of uniform line, 5-25
circle, 5-65
common, in coupled circuits, 6-06
complementary, 5-10
damped, 5-65
driving point, 5-06, 5-10
imago, 5-B ; see also Image impedances
input, of uniform line, 5-26
inverse, 5-09
irregularities, 11-39
lino, a-c bridge method of locating irregularities
in, 11-39
matched, in single-mesh circuits, 6-06
mutual, 5-06
non-matched, in single-mesh circuits, 6-06
loads, 5-43
mechanical, 5-59, 6-03
motional, 5-66
mutual, in coupled circuits, 6-06, 6-07
symbol, 1-73
Impedance, normal, 5-65
open-circuit transfer, 6-38
reciprocal, 5-09
second image, method of obtaining, 6-40
self symbol, 1-73
short- and open-circuit, 6-37
symbol, 1-73
transfer, 5-06, 5-10
transformer for wave-guide component, 10-22
vector, 5-59
two-terminal, 5-07
Imperial Standard Wire Gage, 1-66, 1-69
units, 1-42, 1-50
Impulse noise interference in f-m systems, 8-31,
8-32
Inadequate coupling, 6-09
Inch, abbreviation, 1-71
circular, conversion factors, 1-48
conversion table, 1-47
cubic, abbreviation, 1-71
conversion table, 1-49, 1-50
miner's, conversion table, 1-52
-pound, abbreviation, 1-71
square, abbreviation, 1-72
conversion table, 1-48
Incidence, plane of, 5-53
Incident component, 5-23
waves, symmetrical networks, 5-23
uniform lines, 5-25
Inconel, properties, 2-06
Incremental permeability, defined, 2-60
Index of refraction, 5-53
Indirectly heated cathode, 4-03
Indium, properties, 2-06
Indoor address systems, 16-15
Inductance, coupling, 6-07
leakage, 6-14, 6-23
magnetic, cgs unit, 1-46
conversion table, 1-63
mka unit, 1-46
symbol, 1-46, 1-73
measurement, 11-27
audio-frequency transformers, 6-25
mutual, 1-73, 6-07, 6-13
self, 1-73
standards, 11-22
transmission line, 10-03
variation, 5-40
Induction, intrinsic, 2-57
defined, 2-59
frequency meter, 11-11
low-frequency, 10-88
acoustic disturbance produced by, 10-92
control, 10-93
coupling factors, 10-89
magnetic, 2-57
defined, 2-59
symbol, 1-73
normal, denned, 2-60
residual, defined, 2-60
saturation, defined, 2-60
Inductive coordination, for supply and communi-
cation companies, 10-73
coupling, 10-78, 10-89
influence, 10-75
susceptiveness, 10-80
winding, 11-19
Inductometers, denned, 11-23
Inductor iron core, graphical symbol, 1-76
Inductors, air-core, 3-31
properties, 3-31
best coH shape, 3-33
coil losses, 3-32
design formulas, 3-38
24
INDEX
Inductors, distributed capacitance, 3-32
electrical design considerations, 3-32
ferrous-cored, 3-42
figure of merit, 3-31
form materials, 3-36
graphical symbol, 1-76
high-frequency powdered-core, 3-50
impregnation, 3-37
low-frequency sheet-core, 3-42
mechanical design considerations, 3-36
power factor, 3-31
progressive universal winding, 3-34
shielding, 3-35
solenoid windings, 3-33
specification, 3-38
time constant, 3-31
universal winding, 3-34
wire insulation, types, 3-32
Industrial buildings, sound insulation in. 12-57
roentgonography, tubes for, 4-89
Inerteen, 2-35
Inertia, moment of, cgs unit, 1-46
mks unit, 1-46
symbol, 1-46
Inflection in speech sounds, 12-20
Influence, inductive, 10-75
Information, speed of, 5-28
Infra-black level, 20-16
Infrared radiation, medical uses, 23-06
therapeutic use, 23-08
Initial permeability, defined, 2-60
Inner ear, 12-03
In-phase amplifiers, 7-31, 7-50
Input admittance, conductive component, 4-16
compensating for changes, 4-19
of vacuum tubes, 4-15
reactive component, 4-1 S
capacitance, 4-19
defined, 4-06
variation, 4-19
frequency modulation by, 8-12
conductance, 4-16, 4-22
gap, 4-51
impedance, of a triode, 5-49
of uniform line, 5-26
reaistance, 7-17
transformers, 6-19
leakage resonance, 6-21
made with two-logged core, 6-22
pick-up of, 6-21
shielding of, 6-21
turns ratio of, 6-20
use of shielding cans and, 6-21
Insertion loss factor, 5-15
loss for frequencies in filters, 6-33
phase measurement, 11-34
phase shift, 5-16
Instantaneous values, 1-74
Instrument landing system, 22-14
Insulating liquids, synthetic, 2-52
materials, 2-02, 2-21
dielectric properties, 2-21
gases as dielectrics, 2-53
liquid dielectrics, 2-48
oils, 2-50
phenolic, 2-41
solid dielectric, 2-25
test methods, 2-24
Insulation, calculation of, in building design,
12-69
resistance, 2-23
sound, see Sound insulation
value of rigid materials, 12-64
Insulite, compliance and resistance data in insu-
lation of vibration, 12-62
sound transmission, 12-65
Insurok, 2-38
Intake transformers, use of shielding cans and,
6-21
Integral operator, 5-29
Integrals, 1-12
Integration, by parts, 1-12
constants, 1-13
Intelligibility test, 12-28
Intensifying screen, 23-15
Intensity difference limon, with decibels above
threshold (hearing), 12-10
electric, symbol, 1-73
electric field, cgs unit, 1-46
conversion table, 1-60
mks unit, 1-46
symbol, 1-46
level of sound, 16-13
luminous, 1-42, 14-15
cgs unit, 1-46
mks unit, 1-46
standard of, 1-43
symbol, 1-46
magnetic, symbol, 1-73
magnetic field, cgs unit, 1-46
conversion table, 1-64
mks unit, 1-46
symbol, 1-46
sound, 12-04, 12-57
Interaction factor, 5-15
of electromagnetic systems, 5-65
loss, 5-16
Intercept delay, 5-36
Interelectrode capacitance, 4-14
defined, 4-06
Interference, atmospheric, 10-42
Interlace, odd lino, 20-0(5
Interlaced scanning, 20-05
Intermediate amplifier, 7-56, 7-129
frequencies, "birdiea" in, 7-57
choice, 7-56
examples, 7-57
harmonics and reduction of "tweeta" in, 7-57
high, advantage of, 7-57
interaction between local oscillation and
antenna circuit in, 7-57
subharmonicH, 7-57
frequency amplifier, 7-56
Internal, abbreviation, 1-71
International angntrom unit, 1-79
candle, 1-43
conversion factors, 1-65
joule, 1-57
units of electrical measure, 1-44
Interpolation methods, used in frequency meas-
urement, 11-10
Interstage transformers, 6-19
leakage resonance of, 6-21
pick-up of, 6-21
shielding of, 6-21
turns ratio of, 6-20
Intrinsic induction, 2-57
defined, 2-59
Invar, properties, 2-06
Invariant, properties, 2-06
Inverse anode voltage, 4-05
distance field, 10-30
hyperbolic sine, 1-10
impedances, 5-09
sine, 1-08
Inverted-V antennas, 6-83
Inverters, controlled, 21-09, 21-10
INDEX
25
lonization current, 4-10, 4-11
of gases, 2-54
time of gas-filled oscillators, 7-91
Ionosphere, 10-37
lonthophoresis, 23-03
Indium, properties, 2-06
Iron, 2-61
-aluminum alloys, 2-62
-cobalt alloys, 2-62
-core coils, use in i-f amplifiers, 7-58
-core-transformer, 6-13
effect of heat treatment on magnetic properties,
2-61
gage, 1-67
loss, 2-59
-molybdenum, 2-62
-nickel alloys, 2-62
oxide, properties, 2-10
properties, 2-06, 2-10
-silicon alloys, 2-61
Irradiation, 14-42
Isolantite, 2-38
properties, 2-26
Iso-masking intensity of sound, 12-11
Isotropic dielectrics, 5-53
insulating medium, 5-51
IT calorie, 1-57
Ivory, properties, 2-26
Jack, graphical symbol, 1-76
Joint use of poles, 10-69
Joule, 1-44
abbreviation, 1-71
conversion factors, 1-55, 1-57, 1-64, 1-65
Jute, 2-38
Kanthal, properties, 2-06
Kaolin, 2-38
Karma, properties, 2-06
Kataphoresis, 23-03
Kennelly-Heaviside layer, 10-37
Kerosene, dielectric properties, 2-49
Key, graphical symbol, 1-76
Keystone correction in scanning, 20-11
Kg cal, 1-46
Kilocycles per second, abbreviation, 1-71
Kilogram, abbreviation, 1-71
-calorie, abbreviation, 1-71
conversion factors, 1-57, 1-58, 1-64, 1-65
conversion factors, 1-54, 1-55
-meter, abbreviation, 1-71
conversion factors, 1-56
standard, 1-42
Kilolines, conversion factors, 1-63
Kiloliter, abbreviation, 1-71
conversion factors, 1-49
Kilometer, abbreviation, 1-71
conversion table, 1-47
square, abbreviation, 1-72
conversion table, 1-48
Kilometric waves, 1-80
Kilovolt, abbreviation, 1-71
-ampere, abbreviation, 1-71
reactive, abbreviation, 1-72
conversion factors, 1-60
Kilowatt, abbreviation, 1-71
conversion factors, 1-58
Kilowatt-hour, abbreviation, 1-71
conversion factors, 1-57, 1-64, 1-65
Kinescopes, defined, 15-46
Kinetic energy, 5-57
Klystron amplifier, 4-51
frequency multiplier, 4-52
Klystrons, 4-51
Klystrons, defined, 4-51
employing transit time bunching, 4-51
integral cavity type, 4-51
reflex, 4-54
Knife, high frequency, 23-05
Knots, conversion table, 1-47, 1-52
Koroseal, 2-48
Kriston, 2-34, 2-38
Kromax, properties, 2-06
Kromore, properties, 2-06
Krupp metal, properties, 2-06
Kryptol, properties, 2-10
L to C ratio1, of a tuned circuit, 7-87
of oscillatory circuit, 7-88
Lagrange's principle, 5-59
Lambert, abbreviation, 1-71
Lambert's law, 14-05
Lamicoid, 2-38
Laminae, 2-39
Laminates, 2-38
Lamp in pulse measurements, 9-12
Lamps, ballast, 3-22
exciter, 16-22
fluorescent, 15-37
resistance, 3-22 *
Lanac, 22-28 /
Land measure, area, conversion table, 1^8
length, conversion table, 1-47 r
Laplace transform, 5-34
Larynx, 12-19
artificial, 12-21
speech and, 12-19
Latex, 2-39
Latitude, abbreviation, 1-71
Lattice networks, 5-13
Lava, 2-39
properties, 2-26
Lavite, 2-39
properties, 2-26
Lead-bismuth, properties, 2-06
chloride, properties, 2-10
-in, of radio antennas, 6-62
properties, 2-06, 2-10
-tin alloy, properties, 2-10 *
League (Great Britain), conversion factors, 1-47
League CD". S-), conversion factors, 1-47
Leakage current, 4-10
defined, 4-05
inductance, 6-23
measurements of, audio-frequency trans-
formers, 6-25
of audio-frequency transformer, 6-23
reactance, in driver transformer, 6-22
resonance, of input and interstage transformers,
6-21
Leap year, conversion table, 1-51
Lecher wires, 11-13
Lecture rooms, acoustic design, 12-42
Legal units of measure, 1-42
Length, 1-42, 1-46
cgs unit, 1-46
conversion table, 1-47
mka unit, 1-46
standard of, 1-42
symbol, 1-46
Lenoxite, 2-39
Lenses, 14-09
aberrations, 14-11
bipotential, 14-56
cathode, 14-58
compound, 14-10
cylindrical, 14-54
dielectric, use in antennas, 6-78
26
INDEX
Lenses, electrostatic, 14-51
in air, defined, 14-09
magnetostatic, 14-59
of antennas, 6-78
spherical, 14-54
thick, 14-54
thin, 14-10, 14-54
unipotential, 14-54
Lepidolite, 2-39
Lepidomelane, 2-39
Letter symbols for magnitudes of electrical quan-
tities, 1-72
Level, black, 20-20
television, 20-13, 20-21
volume, 1-41
Libraries, noise levels acceptable in, 12-58
Light, conversion table, 1-65
measurement, 14-17
sense, 14-30
units, 1-43
velocity, 1-79
symbol, 1-73
...Lighthouse tube, 7-89
jcghtning arrester, graphical symbol, 1-76
.-
2-39
, 2-26
Line, i
c !
sequential ft
straight, eau
synchronizing
, 10-03
3
; 20-65
'
amplifier, 7-22 »
circuits, 5-37 .
conductor antem '
detection, 7-79 <•
, 1-71
n6tworks' 5'02
>lex frequency plane, 5-04
ctive, 5-16
stortion, 5-16
driving point impedances, 5-06
Duality, principle of, 5-07
Fourier's theorem, 5-02
mesh equations, 5-05
nodal equations, 5-06
non-sinusoidal currents and voltages, 5-02
power transfer, 5-15
single-mesh circuit, see Circuits, single-mesh
superposition, principle of, 5-02
theorems, 5-12
transfer impedances, 5-06
two-terminal impedances, 5-07
phase, 5-36 .
simultaneous equations, 1-04
velocity, conversion table, 1-52
Xines, distortionless, 5-26
program, radio telephone broadcasting, 16-27
testing, 11-38
transmission, see Transmission lines
uniform, 5-24
characteristic impedance, 5-25
incident and reflected waves, 5-25
input impedance, 5-26
propagation constant, 5-25
.standing waves, 5-25
Lines, uniform, voltage and current relations, 5-24
wire transmission, see Wire transmission linen
Links, conversion factors, 1-47
Linoleum, 12-54
Linseed oil, relation between dielectric constant
and resistivity, 2-51
Lip mic, 22-12
Liquid, abbreviation, 1-71
dielectric absorption, 2-51
dielectric constant, 2-48
dielectric properties, 2-49
dielectric strength, 2-51
dielectrics, 2-48
gallons, conversion table, 1-49
gill, conversion factors, 1-49, 1-50
measure, conversion factors, 1-50
pints, conversion table, 1-49
quarts, conversion table, 1-49
synthetic insulating, 2-52
Lissajous figures, 11-08
Liter, abbreviation, 1-71
conversion table, 1-49
Lithium, properties, 2-06
Litz wire, 3-33
use in i-f amplifiers, 7-58
Live rooms, 12-43
Loaded cable circuits, 10-03
Loading map, 10-51
Loalin, 2-39
Lobing method of microwaves in direction finding,
6-87, 6-88
Localization of sound, 12-18, 16-02
Localizer, runway, 22-14
Location of impedance irregularities, 11-39
of loudspeakers, 16-14
of microphones, 16-05
of radio transmitter, 16-29
Logarithm (common), abbreviation, 1-71
Logarithm (natural), abbreviation, 1-71J
Logarithmic, plate form, 3-57
voltage ratio, 1-38
Logarithms, 1-19
Lohm, properties, 2-06
Lomu, 2-64
London Gage, 1-69
Long ton, conversion factors, 1-54
waves, 10-33
-wire antennas, 6-64
Longitude, abbreviation, 1-71
Longitudinal circuit induction, 10-78
Loop antennas, 6-62, 6-85
Bellini-Tosi, method of direction finding,
6-88
sensitivity to antenna effect, 6-87
coupling, graphical symbol, 1-77
current, 5-26
hysteresis, 2-58
output coupling, 4-47
voltage, 5-26
Loran, 22-31, 22-48
low-frequency, 22-51
performance, 22-51
receiving equipment, 22-50
sky-wave synchronized, 22-51
standard, 22-49
Loss angle, 2-22
equalizers, 5-16, 5-18
factor, 2-22
hearing, with age, 12-08
insertion, 5-15
-phase relation, of a four-terminal network, 5-17
transducer, 5-15
transition, 5-15
transmission, 11-33
INDEX
27
Loudness, computation for sounds with continu-
ous energy spectrums, 12-13
defined, 12-11
levels, 12-11
phon of, 12-11
scale, 12-12
speech, effect of, 12-69
Loudspeaker loads, output transformers, 6-18
Loudspeakers, 16-13
defined, 13-08
efficiency, 13-10
graphical symbol, 1-76
location of, 16-14
performance, 13-18
phasing, 16-14
tests, 13-18
two-way system, 16-23
types, 16-13
Low frequencies, antennas, 6-80
Low-frequency characteristics of audio-frequency
transformers, 6-15
coordination, 10-88
induction, 10-88
acoustic disturbance produced by, 10-92
control of, 10-93
coupling factors in, 10-89
omnidirectional range, 22-31
response of wide-band amplifiers, 7-44
Low-pass filter, 6-33
Low-plate-resistance tube, 7-11
Low-power audio amplifiers, 7-15
radio transmitters, 7-136
resistors, 3-07
Lower limit of hearing, 12-08
L-type networks, 5-13
Lucero, properties, 2-06
Lucite, 2-39, 2-47
Lumarith, 2-36, 2-37, 2-39
Lumen, abbreviation, 1-71
-hour, abbreviation, 1-71
Luminance, 14-16
Luminescence* defined, 15-29
Luminescent materials, 15-29
screens, discharge, 15-44
ion spot in, 15-44
limitations imposed by, 15-43
size and brightness, 15-43
Luminous emittance, 14-17
flux, ogs unit, 1-46
mks unit, 1-46
symbol, 1-46
intensity, 1-42, 14-15
cgs unit, 1-46
mks unit, 1-46
standard of, 1-43
symbol, 1-46
Lungs, speech and, 12-19
Lustron, 2-39
Machine noise, 11-63
M.A.F., 12-05
Magnesium oxide, 2-39
properties, 2-10, 2-26
properties, 2-06
titanate, properties, 2-30
Magnetic armature speaker, 13-15
characteristics, 2-57
measurement, 2-72
coupling, 5-64
currents of antennas, 6-64
field intensity, cgs unit, 1-46
inks unit, 1-46
symbol, 1^6
flux, ogs unit, 1-46
Magnetic flux, conversion table, 1-63
defined, 2-60
mks unit, 1-46
symbol, 1-46, 1-73
induction, 2-57
defined, 2-59
symbol, 1-73
intensity, symbol, 1-73
materials, 2-57
effect of frequency, 2-70
effect of temperature, 2-69
high-permeability, 2-60
magnetic characteristics, 2-57
measurement, 2-72
magnetostriation, 2-70
permanent magnet materials, 2-65
stress, 2-70
moment, cgs unit, 1-46
mks unit, 1-46
symbol, 1-46, 1-73
permeability, 1-43
polarization, symbol, 1-73
potential, conversion table, 1-64
symbol, 1-73
recordings, 13-28
erasing, 13-28, 13-29
magnetic materials for, 13-36
recording, 13-28, 13-29, 13-30
recording media, 13-35
reproduction, 13-28, 13-29, 13-33
scanning, 20-10
speaker, 13-11
storms, 10-46
Magnetization, cgs unit, 1-46
curve, 2-57, 2-68
mks unit, 1-46
symbol, 1-46
Magnetizing force, 2-57
cgs unit, 1-46
conversion table, 1-64
defined, 2-60
mks unit, 1-46
symbol, 1-46, 1-73
Magneto switchboards, 17-03
Magnetomotive force, abbreviation, 1-71
cgs unit, 1-46
conversion table, 1-64
mks unit, 1-46
symbol, 1-46, 1-73
Magnetostatic lenses, 14-59
Magnetostriction, 2-70
defined, 7-92
oscillators, 7-92
Magnetrons, 4-40
anode strapping methods, 4-46
cyclotron frequency, 4-41
frequency stability, 4-49
hole-and-slot, 4-42
input characteristics, 1-11
mode separation, 4-45
methods, 4-47
modes, r-f patterns, 4-42
moding, 4-45
negative resistance, 4-40
non-oscillating, 4-40
oscillating, 4-40
output coupling, 4-47
scaling, 4-45
solid anode, 4-40
tangential resonance, 4-42 fn.
traveling wave, 4-41
operation, 4-42
tuning, 4-50
Magnets, permanent, materials, 2-65
28
INDEX
Magno, properties, 2-06
Mahogany, 12-65
Major diatonic scale, 11-09
Makalot, 2-39
Male voices, 11-60
Malleus of eardrum, 12-02
Manganese-copper, properties, 2-06
-nickel, properties, 2-06
properties, 2-06
Manganin, properties, 2-06
Mantissa, of logarithm, 1-19
M.A.P., 12-05
Marble, properties, 2-26, 12-55
Marbon B, 2-43
Marine navigation, electronic aids, 22-33
radio aids, 22-33
Consol, 22-52
Decca, 22-54
direction-finding system, 22-39, 22-53
facsimile, 22-56
Gee system, 22-52
Lanac, 22-53
Loran, see Loran
miscellaneous systems, 22-56
optimum transmission parameters, 22-57
Popi, 22-55
radar, see Radar
radiobeacon system, 22-36, 22-38
Redar, 22-56
Shoran, 22-52
Sofar, 22-56
Sonar, 22-53
Sonne, 22-52
Teleran, 22-55
Marker, defined, 22-05
used in instrument landing, 22-17
Marsh's patent, properties, 2-07
Masking of sound, 12-11
Masonite, 2-39, 12-52
compliance and resistance data in insulation of
vibration, 12-62
Masonite die stock, 2-39
properties, 2-26
Masonry, 12-55, 12-65
Mass, 1-42, 1-46
cgs unit, 1-46
conversion table, 1-54
electron, 4-14
mks unit, 1-46
per unit volume, conversion table, 1-55
resistivity, 1-61
standard of, 1-42
symbol, 1-46
Master oscillator, 7-88
volume control, 16-07
Matched impedances, in single-mesh circuits,
6-06
Materials, cathode, 4-03
conducting, 2-02
definitions, 2-02
specific, properties, 2-03
wire tables, 2-12
core, for pulse applications, 9-28
diamagnetic, 2-57
dielectric, solid, 2-25
ferromagnetic, 2-57
flexible, coefficients of sound transmission,
12-65
compliance and resistance data in insulation,
12-62
. grain-oriented, 2-61
high-permeability, 2-60
insulating, 2-02
dielectric properties, 2-21
Materials, insulating, gases as dielectrics, 2-53
liquid dielectrics, 2-48
phenolic, 2-41
solid dielectric, 2-25
test methods, 2-24
luminescent, 15-29
magnetic, 2-57
effect of frequency, 2-70
effect of temperature, 2-69
high-permeability materials, 2-60
magnetic characteristics, 2-57
measurement, 2-72
magnetostriation, 2-70
permanent-magnet, 2-65
stress, 2-70
non-magnetic, 2-64
non-polar, 2-22
paramagnetic, 2-57
permanent-magnet, 2-65
typical properties, 2-67
polar, 2-22
porous, sound insulation by, 12-62
properties, Section 2
sound-absorptive, coefficients, 12-48
practical considerations, 12-57
tenebrescent, 15-29
thin rigid, coefficients of sound transmit!"
12-65
Mathematical tables, 1-19
Mathematics, 1-02
Maxima, 1-13
Maximum, abbreviation, 1-71
operating temperature, 2-26
values, 1-74
Maxwell, 1-46
bridge, 2-75, 11-29
conversion factors, 1-63
equations, 1-45, 5-50
Mayer's theorem on reactive networks, 6-61
McBerty automatic telephone system, 17-33
m-derived sections of filters, 6-48, 6-50
image impedance characteristics, 6-53
Mean calorie, 1-57
square root, abbreviation, 1-72
Measure, apothecaries' fluid conversion facto.
1-50
architect's conversion factor, 1-48
board, conversion factor, 1-49
cubic, conversion factor, 1-49
dry, conversion factor, 1-49
land, area, conversion table, 1-48
length, conversion table, 1-47
liquid, conversion factors, 1-50
miscellaneous, conversion factors, 1-47
nautical, conversion table, 1-47
ropes and cables, conversion factors, 1-47
shipping, conversion factor, 1-50
Measurement, absorption, 12-58
capacitance, 11-24
conductance, 4-12
current, 11-16
distance, 9-10
effective resistance, 11-27
electrode capacitance, 1-14
inductance, 11-27
light, 14-17
mu factor, 4-13
of audio-frequency transformers, 6-25
of magnetic characteristics, 2-72
of noise, 12-57
primary electrical quantities, 11-16
pulse, see Pulse measurements
resistance, 11-23
reverberation, 12-48
INDEX
29
Measurement, transconductance, 4-12
transmission, 11-32
use of pulses, 9-02
voltage, 11-17
wire line, 11-32
Mechanical-acoustic system, 5-66
analogue, 5-59
band-pass filter, 11-63
equivalent of heat, 1-79
-fluid system, 5-66
impedance, 5-57, 6-03
reactance, 5-59
recordings, 13-37
recording disks, 13-41
duplication, 13-41
recording instruments used in, 13-37
recording media, 13-40
reproducing instruments, 13-43
magnetic type, 13-43
piezoelectric crystal, 13-43
reproducing media, 13-40
sources of distortion in, 13-45
resistance, 5-59
scanning, 20-07
systems, 5-56
comparison with electrical systems, 5-59
energy, 5-57
vibrations, 5-58
units, 1-42
Medical applications of electricity, 23-01
roeritgenography, tubes, 4-86
Medium-frequency broadcasting, use of direc-
tional antennas and, 6-74
Megagram, conversion factors, 1-54
Megaraeter, conversion factors, 1-47
Megmho, conversion factors, 1-61
Megohms, conversion factors, 1-61
Meissner oscillator, 7-84
Mel, 12-17
Melamine, filled, properties, 2-26
-formaldehyde, resins, thermoaetting, 2-39
glass laminates, 2-39
Melmac, 2-39
Melting point, abbreviation, 1*71
Mensuration, 1-17
Mercury-arc rectifiers, 4-77
properties, 2-07
-vapor tube, defined, 4-04
Merit, figure of, 3-31
Mesh equations, 5-05
Mesitylene, dielectric properties, 2-49
Metal gages, 1-66
oxide-coated, 4-03
tubes, 4-62
Metalloids, 2-03
Meter, abbreviation, 1-71
conversion table, 1-47
cubic, abbreviation, 1-71
conversion table, 1-49
dbm, 11-32
-kilogram, abbreviation, 1-71
conversion factors, 1-57
-lambort, 14-17
square, abbreviation, 1-72
conversion table, 1-48
standard of, 1-42
Methacrylate, 2-39
properties, 2-28
Methane, dielectric constant, 2-54
Methyl alcohol, dielectric properties, 2-49
relation between dielectric constant and resis-
tivity, 2-51
Metric horsepower, conversion factors, 1-58
multiples, 1-47, 1-48, 1-49, 1-54
Metric system, 1-42
ton, conversion factors, 1-54
waves, 1-80
Wire Gage, 1-69, 1-70
Mho, conversion factors, 1-61, 1-62
Mica, 2-39
capacitors, 3-64
cloth, 2-40
glass-bonded, 2-38
paper, 2-40
pasted, 2-40
plate, 2-40
power factor at high frequencies, 2-34
properties, 2-28
Micabond, 2-40
Micanite, 2-40
Micarta, 2-40
Microampere, abbreviation, 1-71
Microfarad, abbreviation, 1-71
conversion factors, 1-62
Micrograms, conversion factors, 1-54
Microhenrys, conversion factors, 1-63
Microhm-centimeters, conversion factors, 1-61
-inches, conversion factors, 1-61
Microhms, conversion factors, 1-61
Micromho, conversion factors, 1-61, 1-62
Micromicron, abbreviation, 1-71
Micron, abbreviation, 1-71
conversion factors, 1-47
square, abbreviation, 1-72
Microphone, 16-04
carbon, 13-26
choice of, 16-05
condenser, 13-24
crystal, 13-25
defined, 13-22
directional characteristics, 13-26
force on, 13-22
graphical symbol, 1-76
location, 16-05
magnetic-armature, 13-25
moving-coil, 13-24
moving-conductor, 13-23
performance, 13-26
placement, 16-05
pressure, 13-22
pressure-difference, 13-23
ribbon, 13-23
tests, 13-26
types, 16-04
Microvolts, conversion factors, 1-60
Microwatt, abbreviation, 1-71
Microwave antennas, 6-86
instrument landing system, 22-28
omnidirectional radio range, 22-30
Microwaves, 1-80
measurements, 11-69
frequency, 11-84
Middle ear, 12-02
Midohm, properties, 2-07
Miles, conversion table, 1-47
nautical, conversion factors, 1-47
per hour, abbreviation, 1-72
square, conversion table, 1-48
statute, conversion factors, 1-47
Military pace, conversion factors, 1-47
Miller capacitance effect of wide-band amplifier
tubes, 7-43
effect, 4-18, 5-49
Milliampere, abbreviation, 1-71
Milligram, abbreviation, 1-71
conversion factors, 1-54
Millihenry, abbreviation, 1-71
conversion factors, 1-63
30
INDEX
Milliliter, abbreviation, 1-72
conversion factors, 1-49
Millimeter, abbreviation, 1-72
conversion table, 1-47
gage, 2-13
square, conversion table, 1-48
Millimetric waves, 1-30
Millimicron, abbreviation, 1-72
Millivolt, abbreviation, 1-72
conversion factorst 1-60
Mils, circular, abbreviation, 1-71
conversion factors, 1-48
conversion table, 1-47
square, conversion factors, 1-48
Mineral oil, 2-52
dielectric properties, 2-49
Minerallac, 2-40
Miner's inch, conversion table, 1-52
Minima, 1-13
Minims, conversion factors, 1-50
Minimum, abbreviation, 1-72
attenuation, 5-12, 6-57
audible field in hearing, 12-05
audible pressure in hearing, 12-05
conductance, 5-08
loss, 5-12
phase, 5-12
reactance, 5-08
resistance, 5-08
resolvable solid angle, 20-02
susceptance, 5-08
visible, 14-43
Minor third, 10-09
Minute, abbreviation, 1-72
Minute (angular measure), abbreviation, 1-72
Minutes (angle), conversion table, 1-51
Minutes (time), conversion table, 1-51
Mixed highs, 20-66
Mixer matching network, 16-08
volume controls, 16-07
Mixing of sound, 16-05
Mks system, 1-42, 1-45
rationalized, 1-44, 1-45, 1-46
unrationalized, 1-44
Mode separation, magnetrons, 4-45
Modes, 4-54, 7-101
cavity resonators, 7-101
quality factor, 7-101
Moding, magnetrons, 4-45
Modulated amplifiers, 7-75
Modulation, amplitude, 7-71
carrier wave, 7-70
cavity, in speech, 12-19
characteristics of pulses and, 9-23
defined, 7-70
distortion, 4-24
frequency, see F-m
frictional, in speech, 12-19
grid, 7-73
Heising amplitude, 7-74
index of frequency modulation, 8-03
modulating wave of, 7-70
percentage, 11-61
phase, see Phase modulation
plate, 7-74
polarity, 20-19
power and efficiency of grid-bias-modulated
amplifiers, 7-73
products, 11-62
pulse, see Pulse modulation
start-stop, in speech, 12-19, 12-20
systems, 7-72
comparison, 7-75
transformer, 6-19
Modulation, types, 7-71
amplitude modulation, 7-71
frequency modulation, 7-71
vocal-cord, in speech, 12-19
Modulator-amplifier coupling circuits, 7-74
Modulators, 7-70
pulse-time, 9-23
thyratron, 9-22
vacuum-tube, 9-22
Modulus (of complex number), 1-06
of elasticity, 2-26
Molded compounds, 2-40
Molybdenum-iron alloys, 2-62
permalloy, 2-62
properties, 2-07, 2-10
Moment, electric, symbol, 1-73
magnetic, symbol, 1-73
of force, conx-ersion table, 1-56
of inertia, cgs unit, 1-46
mks unit, 1-46
symbol, 1-46
Monaural hearing, 16-02
minimum audible pressure (hearing), 12-06
Mond, properties, 2-07
Monel metal, properties, 2-07
Monitoring facilities, 10-09, 16-26
Monochord, 11-12
Monochrome television, 20-02
Monocular television, 20-02
Monoscope, 15-25
Months (average), conversion table, 1-51
Morse code, 18-03
Motion, perception of, 14-44
-picture studios, acoustic design, 12-41
Motional impedance circle, T>-66
joints of wavo guidon, 10-20
Motor noise, 11-64
Motorboating of amplifiers, 7-04
Moving-coil microphono, 13-24
-coil speaker, 13-11
-conductor microphone, 13-23
-conductor speaker, 13-11
-conductor telephone receiver, 13-17
object, resolution of, 20-03
MR Resins, 2-34
Mu factor, 4-13
defined, 4-06
measurement cireuit, 4-13
Multianode tube, defined, 4-75
Multiband sets (radio), i-f amplifiers and, 7-58
Multi-electrode tubes, 5-45
Multiform glass, 2-40
Multigrid tubes, 4-03
Multipath reception, distortion due to, 8-29
of f-m signal, 8-29
transmission, causing frequency modulation,
8-26
downward amplitude modulation and, 8-29
selective fading and, 8-29
Multiple echo, 12-40
product, 1-02
-pulse generator, 9-24
track radar range, 22-30
tuned antenna, 6-80
tuning positions of f-m receivers, 8-17
-unit tube, defined, 4-04
Multiples, defined, 22-05
Multipliers, frequency, 9-13
Multistage amplifier, 7-03
Multivibrators, free-running, 9-18
relaxation oscillation in, 7-84
repetition rate of pulses determined by, 9-19
triggered, 9-18
Mumetal, 2-62
INDEX
31
Musa receiving antennas, 6-83
Muscovite, 2-39, 2-40
Muscular reaction, 23-03
Music, 12-24
audible frequency range of, 12-30
effect of cutoff frequency on orchestral duality.
12-30
effects of distortion, 12-29
optimal reverberation times, 12-75
at different frequencies, 12-75
peak power, 12-24
rooms, acoustic design, 12-41, 12-74
noise levels acceptable in, 12-58
sound insulation, 12-57
scales, 11-09
transmission of, teats for, 12-27, 12-28
Musical instruments, powers produced by, 12-24
Mutual capacitance, 11-24
characteristic, 5-41
conductance, 4-12
of tubes, 6-11
impedances, 6-07
in coupled circuits, 6-07
inductance, 1-73, 6-07, 6-13
Mycalex, 2-38, 2-40
K, 2-38
Mycroy, 2-38, 2-40
Myriagram, conversion factors, 1-54
Myriameter, conversion factors, 1-47
square, conversion factors, 1-48
Myriametric waves, 1-80
n factorial, 1-02
Napierian logarithms, 1-19
Natural frequency of the ear, 12-04
logarithm, abbreviation, 1-71
logarithms, 1-19
Nautical measure, conversion factors, 1-47
miles, conversion factors, 1-47
Navagllde instrument landing system, 22-28
Navaglobe, 22-31
Naval Observatory time signals, 18-40
Navar, 22-29
Navascope, 22-29
Navigation, see also Air navigation; Marine navi-
gation
aide, 22-04
Navy announce equipment, 16-18
NBS gage, 1-69
Negative condenser, 5-59
feedback amplifiers, 7-31, 7-51
effect on distortion, 7-52
glow, 4-50
modulation, 20-19
roaiwtance magnetrons, 4-40
Neoprene, 2-40
properties, 2-28
Neper, 1-37
Nernst filament, properties, 2-10
Nerve conduction, 12-03
fibor, 12-04
Net ton, conversion factors, 1-54
Network switching equipment, for program dis-
tribution, 16-27
Networks, all-pass, 5-21
behavior, 5-29
bridge, 6-13
inverse, 5-09
complementary impedances, 5-10
connective, IOMH equalizers, 5-16, 5-18
losN-phuHO relation, 5-17
phase equnliflerB, 5-16
corrective, 5-16
cutoff frequencies, 6-38
Networks, delay, 5-30
differentiating, 5-29
driving point impedances, 6-35
excess-phase, 5-33, 5-35
four-terminal, see Four-terminal networks
general filter, 6-33
having any prescribed passive transfer function,
5-12
image impedance, 6-37
image transfer functions, 6-37
impedance function, 6-35
integrating, 5-29
inverse or reciprocal impedances, 5-09
lattice, 5-13
linear passive, see Linear passive networks
L-type, 5-13
mesh for, 6-34
method of obtaining second image impedance,
6-40
minimum-phase, 5-33
multi-mesh, 5-05
nodal equations, 6-34
of pure reactances, 5-08
of resistances and capacitances, 5-09
of resistances and inductances, 5-09
oscillatory, transient response, 5-31
parallel type, 6-35, 6-36
phase-correcting, 5-33
reactance function, 6-35
reactive, 5-08
ladder-type, 5-08
Mayer's theorem, 6-61
recurrent, 5-22
uniform lines, 5-24
repeating. 5-30
resonant, 5-30
series-type, 6-35, 6-36
short- and open-circuit, 6-37
simple, transient response, 5-31
symmetrical, 5-23
current and voltage relations, 5-23
impedance relations, 5-23
incident and reflected waves, 5-23
tandem combination, 5-23
T and ir, 5-13
theorems, 5-12
compensation, 5-12
reciprocity, 512
TheVenin's, 5-12
transients in, 5-26
superposition theorem, 5-34
two-terminal, inverse, 5-09
reactive, 6-35
with distributed constants, 5-24
Neural pulses, 12-11
conduction of, to brain, 12-04
Neuritis, 23-06
Neutralization, 7-29
Neutralized receiver, 7-119
Neutralizing transformer, 10-94
New British Standard Wire Gage, 1-69
Newton-meter, conversion factors, 1-56
Nichrome, properties, 2-07
V, properties, 2-07, 2-10
Nickel, 2-03
-chromium, properties, 2-07
-iron alloys, 2-62
properties, 2-07
-silver, properties, 2-07
steel, properties, 2-07
Nickelin, properties, 2-07
Nicraloy, properties, 2-07
Nilvar, properties, 2-07
Nirex, properties, 2-07
32
INDEX
Nitrobenzene, dielectric properties, 2-50
Nitrogen, dielectric constant, 2-54
dielectric properties of liquid, 2-50
minimum sparking potentials, 2-54
Nitron, 2-36, 2-41 j
Nixonite, 2-41
Nixonoid, 2-36, 2-41
Nodal analysis, method, 5-06
equations, 5-06
for networks, 6-34
Nodes, current, 5-26
voltage, 5-26
Noise (noises), abatement, 12-57
allowable residual, 16-02
analysis, examples of, 12-58
analysis of small synchronous motor, 11-64
atmospheric, 10-42
audible frequency range, 12-30
currents, 4-20
effects on articulation, 12-33
extraneous, effects on articulation, 12-33
frequency induction of, 10-74
generated in vacuum tubes, 4-20
in buildings, sound levels of, 12-59
inductive coupling, 10-78
inductive influence, 10-75
inductive mitigation of, 10-82
coupling factors, 10-82, 10-83
influencing factors, 10-82
susceptiveness factors, 10-82, 10-85
inductive ausceptiveness, 10-80 '
levels acceptable in different buildings, 12-58
measurement, 11-36, 11-44, 12-57
out-of-doors, sound levels of, 12-59
positive-ion, 4-22
random, 7-127
range, 12-30
ratio of speech levels to, 12-72
-Deduction factors, 12-69
ceilings and, 12-69
for different amounts of noise, 12-69
walls and, 12-69
windows and, 12-69
-reduction system, 13-49
resistor, 3-13
sound insulation against, 12-57
sound-level meters in measurement, 12-58
sound levels in or near buildings, 12-59
spectrum, 11-59
suppression, 7-126
thermal-acoustic, 12-06
traffic, analysis, example of, 12-58
sound insulation against, 12-57, 12-58
tube, 4-23
Non-linear circuits, 5-37, 7-121
approximate series expansion for plate cur-
rent of a triode, 5-41
capacitance variation, 5-41
characteristics of triode with load, 5-42
current-voltage characteristic, 5-38
harmonic analysis of current for a sinusoidal
applied voltage, 5-4,6
inductance variation, 5-40
multi-electrode tubes, analyses for, 5-45
power series solution, 5-38
solution, 5-38
successive approximations, 5-45
trigonometric series, 5-39
distortion, 5-38
effect of, 12-34
phase characteristics causing f-m distortion,
8-26
Non-loaded cable circuit, 10-03
open-wire lines, 10-03
Non-magnetic materials, 2-64
Non-matched impedances, in single-mesh circuits,
6-06
Non-oscillating magnetrons, 4-40
Non-polar materials, 2-22
Non-uniform delay, f-m distortion and, 8-20
Normal black level, 20-20
induction, defined, 2-60
modes of electromagnetic fields, 7-95
permeability, defined , 2-60
Nose cavities, speech and, 12-19
Null in transmission, f-m distortion and, 8-25)
Number of conductors or turns, symbol, 1-73
of phases, symbol, 1-73
of poles, symbol, 1-73
Numeric, 1-46
Numerical pitch scale, 12-17
Nylon, 2-41
properties, 2-28
Oboe, 12-30
Observation, errors, 1-15
Observations, probable value of several, 1-15
weighted, 1-15
Octane, dielectric properties, 2-50
Octave, 11-09
Octode, defined, 4-04
Odd-line interlace, 20-06
Oersted, 1-46
conversion factors, 1-64
Office buildings, wound insulation, 12-57
Offices, private, noi.se hwdn acceptable in, 12-58
public, noise lovol aeooptablo in, 12-58
Ohm, 1-43, 1-4-1, 1-45, 1-46
abbreviation, 1 -72
-centimeter, defined, 2-02
conversion factors, 1-0 1
-inch, defined, 2-02
-motors, conversion factors, 1-61
per centimeter cube, defined, 2-02
per inetor-gram, 1-61
per mil foot, 1-61
defined, 2-02
per unit weight, 2-16
thermal, 1-65
Ohmax, properties, 2-07
Oils, insulating, 2-52
Old English Wire Gage, 1-69, 1-70
Olive oil, dielectric properties, 2-50
Omnidirectional antennas, using vertical polari-
zation, 6-84
range, 22-18
One-shot amplifiers, 7-31, 7-53
Open-wire circuit, 10-03
Opens, 11-41
Operating conditions, changing, 4-26
range, 4-06
Operational impedance, 5-43
Operator, differential, 5-29
integral, 5-29
Optical system, depth of field, 14-13
depth of foous, 14-13
electron, general theorems, 14-63
light-valvo recording, 13-48
reflective, for television projection, 14-20
stops, 14-13
Optics, 14-02
electron, 14-49
geometrical, 14-02
Format's principle, 14-02
vision, 14-25
Optimal reverberation times, 12-75, 16-03, 16-11
Optimum angle of current flow, 7-131
horn, 6-79
INDEX
33
Orchestras, 12-24
quality, 12-31
Order of modulation, 11-56
Organs of speech, 12-19
Orthicon, 15-26
images, see Imago orthicon
resolution, 15-27
sensitivity, 15-27 '
siRnal-to-noise ratio, 15-27
uniformity, 15-27
Oscillating joints of wave guides, 10-26
magnetrons, 4-40
Oscillations, 5-30
blocking 7-86
condition for persintence, 7-84
conditions for self-oscillation, 7-84
non-linear theory, 7-83
of Ras-filled tubes, 7-91
oscillatory circuit design, 7-86, 7-87
paranitic, in amplifiers, 7-28, 7-29
prevention of, in amplifiers, 7-29
relaxation, 7-84, 7-86
theory of, 7-83
van der Pol's equation for non-linear theory,
7-85
variation in frequency of, in oscillator circuits,
7-94
Oscillator, 7-83, see also Oscillatory circuits;
Vacuum-tube oscillators
at hitfh frequencies, 7-89
audio-froquonny, 11-89
BarkhauHori, 7-91
buffer amplifier, 4-52
circuilH, conventional, 7-84
dUNHifirtations, 7-83
Ooipittn, conytant frequency circuit derived
from, 7-88
corxHtant-frotiuonoy, 7-87
wyHtnl, 7-92
do/mad, 7-83
eliBtortionloHH, 7-90
etactrutnoohanittal, 7-91
equivalent circuit, 9-23
Kan-filled, deiontaation time of gas in operation,
7-91
ionization time of gas in operation, 7-91
Hartley, 7-93
hetesrodyno, 1 1-31
interpolating, 11-10
frequency compariwon with, 11-10
magneton trietion, 7-92
piezoelectric, crystal, 7-92
plate modulation of, and cla«« C amplifiers, 7-85
pulne-modulated carrier-frequency, 9-22
pul«o modulation, 9-21
quarts crystal, 7-92
r-f, 11-00
roHifitanca-eapacitance tuned, 7-90
Holf-cxmtnd, 4-49
separately excited, 7-88
niuuiioUial, 7-K6
Bpark-ftup, 7-94
synchronization, 7-88
tracking of Hiiperhoterodyne receiver, 7-121
triodo, 7-89
tuned-plato tuned-grid, 7-83
timing-fork, 7-91
-typo reiayw, elootromatfnetioally operated,
21-23
ol«d.roHtati(!ttIly operated, 21-23
UHo of quartz, 7-92
two of Rochollo «alfc, 7-92
une of totirmalino, 7-92
velocity variation, 11-92
Oscillatory circuits, design, 7-86, 7-87
ordinary, resonant concentric lines in, 7-SP
transients, 5-27
Oscillograph tubes, multiple gun, 15-47
-type cathode-ray tubes, see Cathode-ray tuoes,
oscillograph-type
Oscilloscopes, cathode-ray, 2-76
pulse measurements by, 9-10
synchroscope type, 9-12
Osmium, properties, 2-07
Ossicles, 12-02
Ostwald calorie, conversion factors, 1-57
Ounce, abbreviation, 1-72
conversion factors, 1-54, 1-55
fluid, conversion factors, 1-49, 1-50
-foot, abbreviation, 1-72
-inch, abbreviation, 1-72
Outdoor address systems, 16-15
Outer ear, 12-02
Output capacitance, denned, 4-06
gap, 4-51
power, standardization, 11-96
transformers, 6-17
wave spectrum, 1 1-56
Overall selectivity curve, in coupled circuits, 6-10
Overbunching, 4-53
Owen bridge, 11-28
Oxide-coated metal, 4-03
Oxygen, dielectric constant, 2-54
minimum sparking potentials, 2-54
Ozite, 15-54
Ozokerite, 2-41
properties, 2-28
Pace, military, conversion factors, 1-47
Pad, 6-05
-type resistors, 3-09
Padding condenser, 3-56
Paging systems, 16-16
Painting of acoustic material, 12-57
Paired echoes, 5-33
Palladium, properties, 2-07
Palm, conversion factors, 1-47
Pancake winding, 6-24
Panel dial telephone system, 17-17
decoder, 17-20
dial pulse register circuit, 17-20
operation, 17-23
panel-type selector, 17-17
sequence switch, 17-20
Panelyte, 2-41
Paper, insulating, 2-41
kraft, properties, 2-28
Parabola, cutoff, 4-40
equation, 1-05
mensuration, 1-17
Parabolic reflectors of antennas, 6-78
Paraboloid cylinders of reflectors of antennas,
6-78
mensuration, 1-18
Paraboloidal antenna, 6-63
Paraffin, properties, 2-28
waxr relation between dielectric constant and
resistivity, 2-51
Paragonite, 2-39
Paragutta, 2-41
Parallel resonant circuits, 6-04
tuning, 6-05
type networks, 6-35, 6-36
Parallelogram, mensuration, 1-17
Paramagnetic materials, 2-57
Parameters, image, see Image parameters
Parasitic oscillation in amplifiers, 7-28, 7-29
Paraxial rays, denned, 14-07
34
INDEX
Partitions, rigid, coefficients of sound transmis-
sion, 12-65, 12-66
Parts, integration by, 1-12
Pass band of filters, 6-33
image impedance and, 6-36
image transfer constant, 6-36
Passive circuits, attenuators, 6-05
elements, 6-02
pads, 6-05
Pattern sharpaess, defined, 22-05
PBX boards, see Private branch exchange (PBX)
boards
Peak angle swing, frequency modulation and, 8-06
detector, 7-79
(or crest) forward anode voltage, defined, 4-05
(or crest) inverse anode voltage, denned, 4-05
power measurements, 11-81
speech power, 12-22
voltmeter, 11-17
Peanut oil, dielectric properties, 2-50
Pecks, conversion factors, 1-50
Peerless, properties, 2-07
Pennyweights, conversion factors, 1-54
Pentanes, conversion factors, 1-65
dielectric properties, 2-50
Pentode, characteristics, 4-37, 4-38, 4-39
defined, 4-04
graphical symbol, 1-77 ;
power amplifiers, 7-13
suppressor-grid, 4-03
type tubes, 6-11
voltage amplifiers, 7-11
Perbunan, 2-35, 2-41
Percentage articulation for rooms, 12-69
modulation, measurement, 11-61
Perception, of depth, 14-45
of motion, 14-44
temporal aspects, 14-33
Perch, conversion factors, 1-47
of stone, conversion factors, 1-49
Period, hyperbolic, 1-10
symbol, 1-73
transient, 5-27
trigonometric, 1-08
Periodic waves, frequency spectrum, 5-28
Permalloy, 2-62, 2-70
powdered, 2-62
Permanent-magnet materials, typical properties,
2-67
Permeability, 2-57
a-c, defined, 2-60
curves, 2-57
incremental, defined, 2-60
initial, defined, 2-60
magnetic, symbol, 1-73
normal, defined, 2-60
relative, cgs unit, 1-46
mks unit,-46
symbol, 1-46, 1-73
reversible, 2-59
defined, 2-60
space, 1-44
cgs unit, 1-46
mks unit, 1-46
symbol, 1-46
superposed, 2-59
tuning, 3-52
Permeameters, 2-74
Permeance, symbol, 1-73
Permendur, 2-62
Permenorm, 2-62
Perminvars, 2-62
Permittivity, 1-73
Permutations, 1-03
Petrolatum, 2-41
properties, 2-28
Petroleum, dielectric properties, 2-50
ether, dielectric properties, 2-50
oils, relation between dielectric constant and
resistivity, 2-51
Phantom circuit, 10-03
transposition, 10-78
Pharynx, speech sounds and, 12-20
Phase angle, of resistor, 1 1-24
symbol, 1-73
constant, symbol, 1-73
delay, 5-36
difference, 2-22
distortion, 20-05
linear, 5-36
modulation, see also Frequency modulation
discriminator action of detectors, 8-03, 8-19
Phasitron tube used in, 8-11
quasi-mechanical method, 8-11
sideband distribution for, 8-06
systems, 8-02
voltage vector with, 8-03
modulators used for emergency transmitters,
8-15
propagation, velocity of, 5-25
shift, insertion, 5-16
minimum, 5-17
slope, 5-36
swing measurement of f-m equipment, 8-08
velocity, 5-36
Phasing of speakers, 16-14
Phasitron tube, frequency modulation using, 8-1 1
Phenix, properties, 2-07
Phenol, dielectric properties, 2-50
fiber, 2-41
Phenolic cast, properties, 2-28
glass base, power factor at high frequencies,
2-34
insulating materials, 2-41
laminates, properties, 2-28
mica filled, power factor at high frequencies,
2-34
moldings, properties, 2-28
paper base, power factor at high frequencies,
2-34
resins, 2-41
Phenolite, 2-41
Phi-phenomenon, 14-44
Phlogopite, 2-39, 2-41
Phon of loudness levels (sound), 12-11
Phonetic printing, visible speech and, 12*21
speech power, 12-22
Phonograph, distortion, 12-35
Phosphor-bronze, properties, 2-07
crystals, luminescence-active centers in, types,
15-36
Phosphorescence, defined, 15-30
Phosphors, characteristics, 15-37
corpuscular excitation, 15-34
defined, 15-31
mechanisms, 15-34
photon excitation, 15-35
preparation and notation, 15-32
Phot, 1-46
Photocells, barrier, 15-13
Photoconductive cells, 15-11
amplification, 15-13
frequency response, 15-12
sensitivity, 15-12
wavelength response, 15-11
Photoelectric cathode, graphical symbol, 1-77
cell, 16-22
relays, 21-21
INDEX
35
Photoelectric tube, 15-02
Photoemissive cells, 15-04
amplification, 15-10
gas-filled, 15-06
measuring circuits for use with, 15-09
sensitivity, 15-07
vacuum, 15-06
Photofluorograph, 23-16
Photographic sound recordings, 13-47
flash-lamp system, 13-51
Kerr cell system, 13-52
light- valve system, 13-48
noise-reduction system, 13-49
reflecting-galvanometer system, 13-50
requirements, 13-54
sound-on-film system, 13-52
sound tracks, variable-area, 13-53
variable-denisty, 13-53
transparencies, 20-03
Photoluminescence, defined, 15-30
Photometry, 14-14
illuminance, 14-16
luminance, 14-16
luminous efficiency in, 14-15
luminous emittanoe, 14-17
luminous intensity in, 14-15
physical, 14-17
relations in non-visual optical systems, 14-18
units in, 14-17
visual, 14-17
Photomultiplier tube, 15-10
Photon excitation, of phosphors, 15-35
Photoresponsive devices, 15-02
classification, 15-02
photoelectric, 15-02, 15-16
thermal, 15-02, 15-03
Phototubes, 4-02
defined, 4-04
graphical symbol, 1-76, 1-77
Photovoltaic cells, characteristics, 15-15
Physical constants and ratios, 1-79
Physiological emf, 23-08
requirements, television, 20-02
Piano, 12-25, 12-30
Piccolastic, 2-41
Piccolo, 12-25, 12-30
Pick-up tubes, application, 15-29, 20-07
requirements, 15-19, 20-30
Picture display devices, 20-08
receivers, block diagram, 9-07
television, 20-03
transmission, by pulses, 9-06
transmitters, block diagram, 9-07
scanning functions, 9-07
synchronizing functions, 9-07
tubes, defined, 15-46
deflection and focus, 15-47
Piezoelectric crystal oscillator circuits, 7-93
crystal oscillators, 7-92
crystals, 13-55
application, 13-68
defined, 13-55
definition of effects, 13-56
microphone, 13-25
plate, graphical symbol, 1-76
properties of crystal in oscillators, 7-93
telephone receiver, 13-18
Pigmentation, 23-07
Pinna of ear, 12-02
Pint, abbreviation, 1-72
conversion factors, 1-49, 1-50
Pipe organ, 12-25
Pistons, 13-04
enclosed back, 13-05
Pistons, multiple, 13-04
Pitch, 2-35
Pitch (sounds), change, 12-16
comparisons, 12-16
half, judgments of, 12-16
intervals, 12-17
numerical scale, 12-17
of low-frequency tones, auditory nerves and,
12-03
variation, 12-16
Placement of microphone, 16-05
of speaker, 16-13
Placet, properties, 2-07
Planck constant, 1-79
Planck's radiation law, 15-30
Plane angle, conversion table, 1-51
of incidence, 5-53
waves, progressive, 5-51
Plant broadcast systems, 16-16
Plaskon, 2-41
Melamine, 2-39
Plastacele, 2-36, 2-41
Plaster, 12-54, 12-55, 12-66
board, 12-65
Plate characteristic, 4-11
current detector, resistance coupled to succeed-
ing amplifier tube, 7-78
currents, denned, 4-05
of a triode, 5-44
denned, 4-04
efficiency, 7-09
forms of capacitors, 3-57
graphical symbol, 1-77
-grid transconductance, 5-43
modulation, 7-74
piezoelectric, graphical symbol, 1-76
power, of receivers, 7-106
resistance, 4-11
transformer, 6-26
voltage, defined, 4-05
Platinite, properties, 2-07
Platinoid, properties, 2-07
Platinum-cobalt alloys, 2-68
-iridium, properties, 2-08
properties, 2-07, 2-08
-rhodium, properties, 2-08
Plai, 2-41, 2-42
Pleurisy, 23-06
Pleriglas, 2-39, 2-41, 2-47
Pliolite, 2-41, 2-43
Plosive release in visible speech, 12-21
Plug-in type resistors, 3-09
Pneumatic speaker, 13-17
Point source of radiation, 13-03
Polar diagram, 4-49
materials, 2-22
Polarity of modulation, 20-19
Polarization, electric, symbol, 1-73
magnetic, symbol, 1-73
television, 20-20
Pole, conversion factors, 1-47
lines, 10-49
basic conductor loadings, 10^51
guying, 10-55
joint use, 10-50
loading calculations, wire equivalents, 10-52
strength, magnetic, cgs unit, 1-46
TnVs unit, 1-46
symbol, 1-46, 1-73
Polectron, 2-41, 2-47
Poles, cross-arms on, 10-55
open wire, 10-55
spacing, 10-55
treatment, 10-54
36
INDEX
Police radio, 16-35
equipment, 16-37
frequency allocation, 16-36
power and range of, 16-37
Polyamides, 2-41
Polychlorostyrene, power factor at high frequen-
cies, 2-34
Polycylindrical sound diffusers, 12-70, 12-71
Polydichlorostyrene, 2-42
properties, 2-28
Polyethylene, 2-42
power factor at high frequencies, 2-34
properties, 2-28
Polyflex, 2-42
Polystyrene, 2-34, 2-42
modified, 2-42
power factor at high frequencies, 2-34
properties, 2-28
Polytetrafluoroethylene, 2-42
power factor at high frequencies, 2-34
properties, 2-28
Polythene, 2-42, 2-47
Polyvinyl acetal resin, 2-34
carbazole, power factor at high frequencies,
2-34
Poncelet, conversion factors, 1-58
Pool cathode, denned, 4-75
graphical symbol, 1-78
-cathode tubes, 4-75
available, 4-76
classification, 4-77
tube, denned, 4-75
Porcelain, 2-42
properties, 2-10, 2-28
wet process, power factor at high frequencies,
2-34
Porches, television, 20-16
Porous materials, 12-62
Positive-ion current, 4-03
modulation, 20-19
noise, 4-22
Potassium, properties, 2-08
Potential difference, 1-60
electric, symbol, 1-73
gradient, cgs unit, 1-46
conversion table, 1-60
inks unit, 1-46
symbol, 1-46
' magnetic, symbol, 1-73
magnetic vector p., symbol, 1-73
retarded scalar, symbol, 1-73
retarded vector p., symbol, 1-73
Potentiometers, 3-17
carbon composition type, 3-20
defined, 3-02
step-type, 3-20
wire-wound, 3-18
Pound, abbreviation, 1-72
British imperial, 1-42
conversion factors, 1-54, 1-55
-foot, abbreviation, 1-72
conversion factors, 1-56
-inch, abbreviation, 1-72
per square foot, abbreviation, 1-72
per square inch, abbreviation, 1-72
XT. S. avoirdupois, 1-42
Poundals, conversion factors, 1-55
Power, active, cgs unit, 1-46
inks unit, 1-46
symbol, 1-46, 1-73
amplification, 7-03
amplifiers, 7-131
Doherty, 7-131, 7-132
negative feedback applied to, 7-133
Power amplifiers, plate-circuit modulation used
in, 7-132
r-f harmonic radiation, 7-132
shunt neutralization employed in, 7-132
apparent, symbol, 1-73
circuit transposition, 10-79
conversion table, 1-58
factor, 2-22
abbreviation, 1-72
symbol, 1-73
gain of receiving antennas, 6-72
level, 1-41
loss, 2-22
measurement, 11-102
musical instruments, 12-24
pulse, 9-10
radiated, 5-52
reactive, cgs unit, 1-46
mks unit, 1-46
' symbol, 1-46, 1-73
reference levels, 1-41
requirements, 16-13
series solution, 5-38
speech, 12-22
supply, 7-106
systems, coordination of communication and,
10-67
transfer, 5-15
insertion loss, 5-15
insertion phase shift, 5-16
reflection factor, 5-15
symmetry factor, 5-15
transition loss, 5-15
transformers, 6-26
calculation of performance, 6-29
construction, 6-27
copper loss of windings, 6-29
core lows, 6-28, 6-29
design procedure, 6-28
efficiency, defined, 6-30
flux density, 6-28
heating, 6-29
insulation, 6-29
regulation of secondary winding, 6-30
size, 6-26
volt-ampere rating, 6-26
-type resistors, layer windings, 3-07
non-inductive windings, 3-07
Poynting's vector, 5-51
symbol, 1-73
Practical electrical units, 1-44
Precision-type resistors, 3-07
Preferred resistance values, 3-12
Premier, properties, 2-08
Preselector, 7-119
Pressboard, 2-43
properties, 2-28
Pressure, audible, 12-05
cgs unit, 1-46
conversion table, 1-56
difference microphone, 13-23
mks unit, 1-46
symbol, 1-46
wind, 10-53
Prestite, 2-43
properties, 2-28
Primary daytime coverage, 16-32
electrical quantities, 11-16
feed of microwave antennas, 6-77
Principal diagonal (determinant), 1-04
night-time coverage, 16-32
service, 16-32
Prisms, electron, 14-62
INDEX
37
Prisms, with parallel sides and parallel ends, men-
suration, 1-18
Private branch exchange (PBX) boards, dial
units, 17-116
equipment, 17-114
manually operated, 17-114
protection, 17-116
Probable error, in result calculated from means of
several observed quantities, 1-16
of any one of several observations, 1-16
of arithmetical mean, 1-16
Product curve, of permanent-magnet materials
2-65
Program amplifier, 16-09
linos, classes, 16-27
service, facilities, 17-103
requirements, 17-101
special features, 17-105
volume range, 16-34
Progression, arithmetical, 1-02
geometrical, 1-02
Progressive plane waves, 5-51
universal winding, 3-34
Projection practices, 16-21
tubes, defined, 15-46
Propagation constant, 5-25
symbol, 1-73
wave, Huygen's principle, 6-76
Properties, of materials, Section 2
Psychoses, 23-04
Public-address systems, 16-14
classification, 16-14
Pulling figure, 4-49
Pulsating sphere, 13-03
Pulse amplifiers, 7-31, 7-55, 9-14
coupling time constant, 9-14J
i-f, 9-14
recovery time, 9-14
riso time of input pulse and, 9-14
video frequency, 9-15
amplitude, measurement of, by comparison
with continuous wave, 9-11
pulac measurements and, 9-10
broad television, 20-13
circuits, 9-13
delay lines, 9-28
frequency counters, 9-13
frequency dividers, 9-13
frequency multipliers, 9-13
vacuum tubes and, 9-26
coding, 9-02
counter, elementary, 9-25
frequency control, 8-14
detection, output envelope of pulsed oscillator,
9-06
with background noise, 9-05
with echo, 9-06
detectors, 9-24
double-pulse decoder, 9-26
duration, 9-11
measurements, 9-10
by bolometer bridge, 9-11
by oscilloscope, 9-10
calorimeter used in, 9-12
lamp uyed in, 9-12
pulae frequency, 9-12
modulation, 9-05
basic types, 9-03
of an owcillator, 9-21
typca, 9-03
used in low-speed and high-speed code trans-
mission, 9-05
narrowing in pulse shaping circuits, 9-15, 9-16
power, pulse measurements and, 9-10
Pulse selection, 9-25
by pulse duration, 9-25
coincidence mixer tube and, 9-25
shaping circuits, baseline clamping, 9-17
clamping or d-c reinsertion, 9-17
differentiation of pulse in, 9-15
narrowing by r-c differentiation, 9-16
narrowing by use of delay line, 9-16
narrowing by use of oscillatory circuit, 9-16
operating conditions of tubes in, 9-15
pulse narrowing in, 9-15
pulse widening, 9-16
squaring a sine wave, 9-15
systems, communication, 9-05
computers, 9-08
multiplex operation of several channels by,
9-05
techniques, 9-02
electronic, 9-02
thyratrons, 4-69
-time modulation, multiplex operation of sev-
eral channels by, 9-05
•time modulator, 9-23
timing circuits, 9-19
blocking oscillators, pulse duration and,
9-20
delay line used to control repetition rate of
pulses in, 9-19
duration of pulses and, 9-20
transformers, 6-32, 9-27
wave forms, 9-27
tubes, 9-26
Pulsed waves, 9-02
comparison of continuous waves and, 9-02
Pulses, 9-02
core materials for application, 9-28
delayed, 9-21
circuits, 9-21
duration, 9-11
equalizing, 20-13, 20-17
frequency spectrum of, 9-11, 9-12
from diverse locations, 9-10
modulating, basic types, 9-03
characteristics, 9-23
phase modulation, 9-26
picture transmission, 9-06
reflection, 9-10
repeating, average value of power, 9-11
details, 9-12
frequency of, 9-12
return, 9-10
speed of information and, 9-03
square, widening of, by reduction of frequency
bandwidth, 9-04
synchronizing, 20-16
time modulation, 9-26
timing, distance measured by, 9-09
types of modulation, 9-03
use in measurements, 9-02
use in signaling, 9-02
Pumped rectifier, defined, 4-75
Pupil (eyes), 14-27
Pure coupling in passive circuits, 6-07
imaginary, 1-06
vowels, 12-20
Pushbutton sets, broad i-f amplifiers used in. local
osciUator in, 7-60
tuners, tests on, 11-47
Pushing, defined, 22-06
PushpuU amplifiers, 7-10
output transformer, 6-18
Pylon antenna, 6-86
Pyralia, 2-36, 2-43
Pyramid, right, mensuration, 1-18
38
INDEX
Pyramidal horn, radiation from wave guides
formed by, 6-63
Pyranol, 2-52
Pyrex, 2-43
Pyridine, dielectric properties, 2-50
Pyrotenax, 2-39
Pyroxylin, 2-43
0,3-48
air gaps, 3-49
core loss and, 3-52
for mode of cavity resonator, 7-101
maximum, 3-49
optimum, 3-48
optimum permeability, 3-49
Q Max., 2-43
Quadded cable, 10-03
Quadrants, conversion table, 1-51
Quadratic equation, 1-03
Quadripoles, equivalent, 5-13
Quality of a reactor, symbol, 1-73
Quantities, complex, 1-06
electrical, letter symbols for magnitudes, 1-72
imaginary, 1-06
Quantity, electrical, cgs unit, 1-46
conversion table, 1-58
mks unit, 1-46
symbol, 1-46
of heat, cgs unit, 1-46
mks unit, 1-46
symbol, 1-46
Quarter, conversion factors, 1-54
section, conversion factors, 1-48
wave antennas, 6-36, 6-70
Quarts, abbreviation, 1-72
conversion factors, 1-50
liquid, conversion table, 1-49
Quartz, 13-58
' crystal oscillators, 7-92
Dauphine twinning, 13-60
defects, 13-60
fused, 2-43
properties, 2-28
physical properties, 13-59
power factor at high frequencies, 2-34
principle cuts, 13-62
properties, 2-10
resonators, 11-12
use in oscillators, 7-92
use in piezoelectric crystals, 13-56
useful orientations, 13-60
Quasi-optical antennas, 6-63
Quasi-steady-state analysis for f-m distortion,
8-26
Quiescent point, defined, 4-06
Quinoline, dielectric properties, 2-50
Quintal, conversion factors, 1-54
Radar, 22-44
antenna system, 22-46
beacons, 22-47
marker, 22-48
reflector, 22-48
carrier frequency, 22-45
duty cycle, 22-45
indicator, 22-46
installation, 22-47
maintenance, 22-47
maximum range, 22-46
minimum range, 22-46
monitor for airport traffic control, 22-24
operation, 22-47
power supply, 22-46
presentation, 22-47
Radar, principles, 22-44
pulse repetition rate, 22-45
receiver, 22-46
resolution, 22-46
synchronizer, 22-46
timer, 22-46
transmitter pulae width, 22-45
transmitters, 22-46
Radial deflection tubes, 15-47
Radians, conversion table, 1-51
Radiated powers, 5-52
Radiation, 5-49
acoustic, 13-03
efficiency of antennas, 6-68
electromagnetic, 5-49
in free space, 10-29
of microwave antennas, 6-77
resistance of antennas, 6-68
secondary, 23-15
soft, of x-ray, 4-82
thermal, 15-29
Radiator, elementary, 5-52
Radio antennas, 6-62
flat-top of, 6-62
general function and description, 6-62
lead-in, 6-62
loop, 6-62
broadcast, 16-25
frequencies, 11-14
amplifiers, 7-22, 7-24
markers, 22-09
-phare, 22-05
police, 16-35
equipment, 16-37
frequency allocation, 16-36
power and range, 16-37
propagation, 10-29
range, defined, 22-05
low-frequency, 22-06
visual two-course, 22-08
receivers, 7-115; see also Receiver circuits;
Receivers
antenna coupling circuit, 7-115
functions, 7-115
gain and selectivity sources, 7-58
high-inductance antenna coupling of, 7-115
spectrum, general view, 10-29
stations, range of, 10-47
studios, 12-02
noise levels acceptable in, 12-58
telegraph, control channels, 18-60
bandwidths, 18-61
recorder drive, 18-61
tone keyers, 18-60
tone signal converters, 18-60
fading, reduction of, 18-57
frequencies, 18-56
frequency shift keying, 18-58
interference, 18-58
receiver sites, 18-56
traffic office, equipment, 18-58
transmitter sites, 18-56
telephone broadcasting, 16-25
fidelity requirements of system, 16-33
frequency allocation, 16-30
program distribution systems, 16-27
program lines, 16-27
station service, 16-32
transmitter plant, 16-28
telephone systems, 17-54
coastal harbor and inland waterways, 17-59
highway mobile, 17-59
installation, 17-66
railway mobile, 17-60
INDEX
39
Radio telephone systems, rural subscriber, 17-60
special emergency, 17-61
two-way operation, 17-62
interconnecting with two-wire extensions,
17-63
with four-wire terminals, 17-62
telephone transmission, 17-61
operational methods, 17-61
privacy, 17-62
requirements , 17-65
single sideband, suppressed carrier, 17-61
spread sidebands and carrier, 17-61
two sidebands and carrier, 17-61
two sidebands, suppressed carrier, 17-61
transmission, national and international regu-
lations, 7-120
transmitters, 7-129
a-rn, 7-120
audio amplifiers, 7-134
circuit Q and, 7-130
frequency control, 7-129
harmonic amplifiers and, 7-130
high-power, 7-136
audio equipment, 7-136
incidental phase modulation, 7-136
installation, 7-134
intermodiate-r-f amplifiers, 7-129
interstage coupling circuits, 7-129
multiple resonances and, 7-129
parasitics and, 7-129
low-power, 7-136
modulation characteristics measurements,
7-185
negative feedback and, 7-133
oscillator power, 7-129
power amplifiers and, 7-131
rectifier and power equipment, 7-137
scope, 7-129
fltibfltation for power, 7-137
unmodulated intermediate amplifiers, 7-130
waverneter, 11-12
waves, pulsed, 9-02
Radiohm, properties, 2-08
Radiometer, 15-04
Radiosondes, 22-13
Radiothermy, 23-04
Range, auditory, 9-06
muwo, 12-30
of radio station, 1 0-47
Ranges, standard r-f, 1-80
Raster, 20-03
Rate of doing work, conversion table, 1-58
Ratio, aopect, 204)3, 20-20
f-m detection, distortion and, 8-29
logarithmic voltage, 1-38
of electrostatic to electromagnetic unite,
1-79
of maas of H to mass of electron, 1-79
physical constants and, 1-79
-typ© frequency detectors, 8-21
Rationalized mke units, 1-45
Ray acoustics of rooms, 12-41
Rayo, properties, 2-08
Rayon, 2-43
R-c coupled amplifiers, 7-04, 7-90
tuned oscillators, 7-90
RCA broadside arrays antennas, 6-65
Reactance, oapacitative r., symbol, 1-73
coupling, 6-07, 6-08, 6-09
function of networks, 6-35
inductive r., symbol, 1-73
minimum, 5-08
mutual r., symbol, 1-73
self r., symbol, 1-73
Reactance, symbol, 1-73
tubes, frequency modulation by, 8-12
Reactive component of input admittance, 4-18
factor, symbol, 1-73
kilovolt-ampere, abbreviation, 1-72
power, cgs unit, 1-46
mks unit, 1-46
symbol, 1-46
volt-ampere, abbreviation, 1-72
Reactors, audio frequency plate, 3-48
rectifier-filter, 3-48
saturable, 3-48
Rear feed for reflectors of antennas, 6-86
Receiver circuits, compensated volume control,
7-126
distribution of amplitude, 7-128
distribution of envelope amplitude vs. time,
7-128
effect of audio transformer on fidelity, 7-126
random noise, nature of, 7-128
tone control, 7-126
power supply, 7-106
typical, 7-107
Receivers, 7-115; see also Radio receivers; Re-
ceiver circuits
a-c operated, filament power for, 7-106
aircraft, 22-21
all-wave, 7-124
audio output, 7-124, 7-125
automatic direction finder, 22-11
automatic volume control, advantage of, 7-125
crystal detector, 7-117
fidelity characteristics, 7-125
f-m, see F-m receivers
f-m — a-m, 8-17
circuit diagram, 8-18
Johnson noise, 7-127
neutralized, 7-119
noise factor, 7-127
noise suppression, 7-126
noise suppressor circuit, 7-127
one-tube superregenerative, 7-118
picture, 9-07
radio, see Radio receivers
random noise, 7-127
receiving tubes in, voltage supply for plate cir-
cuits of, 7-106
reception of continuous wave code signals,
7-124
reduction of effect of fading signals, 7-125
regenerative, 7-117
objection to, 7-117
oscillation, 7-117
regenerative detector, 7-124
circuit, 7-124
resistance-coupled audio amplifier, 7-125
shot effect in vacuum tubes, 7-127
six-tube superheterodyne, 7-120
superheterodyne, combined first detector and
oscillator, 7-119
frequency converter, 7-119
preselector, 7-119
superregeneration of the blocking type in, 7-117
telephone, see also Telephone receivers
graphical symbol, 1-76
simple, 5-65
television, 20-46
thermal agitation, in circuit resistances, 7-127
tuned r-f, 7-118
neutralization use to eliminate oscillation,
7-119
regeneration in multistage amplifiers, 7-118
tuning indicators, 7-124
types, 7-117
40
INDEX
Receiving tube classification chart, 4-28
Reciprocal impedances, 5-09
Reciprocity theorem, for linear networks, 5-12
of Lord Rayleigh, 10-29
Recording practices, 16-19
studios, noise levels acceptable in, 12-58
polycylindrical sound diffusers, 12-71
sound insulation, 12-57
wave analyzer, 11-65
Recordings, see Magnetic recordings; Mechanical
recordings ; Photographic sound recordings
Recovery time in pulse amplifier, 9-14
Rectangular hyperbola, equation, 1-05
wave guides, 10-11
bends, twists, and angles, 10-21, 10-22
Rectification diagrams, 7-79
Rectifier circuits, 7-110
class B modulator, 7-113
control systems, 7-114
double output, 7-110
double-stage filter, 7-112
filter chokes, 7-113
high-voltage transformers, 7-110
rectifier control systems, 7-114
rectifier-tube operation, 7-113
single-stage filter, 7-112
telephone, linear amplifier, 7-112, 7-113
tube, 1-76, 4-28
tube heater delay, 7-114
tube-failure prediction, 7-114
wave form, 7-107
pumped, defined, 4-75
tubes, mercury-vapor, 7-108
output characteristics, 7-108
supply filter, 7-108
Rectifiers, 3-25
application, 21-03
circuit, 21-03
classification, 4-03
contact, 11-17
controlled, 21-09
double output, 7-110
electronic, 21-02
gas-filled, 4-03
high vacuum, 4-03
ignitron, 21-10
mercury-arc, 4-77
non-controlled, 21-08
transformers used in, 7-110
types used in transmitters, 7-109
vacuum tube, 7-106
Recurrent networks, see Networks, recurrent
Red cadmium line, wave length, 1-79
Redray, properties, 2-08
Reference level, 1-41
noise, 11-37
pressure of sound, 12-05
volume, 16-10
Reflected component, 5-23
waves, symmetrical networks, 5-23
uniform lines, 5-25
Reflecting field, 4-54
Reflection, 14-02
at spherical surfaces, 14-05
coefficient plane, 4-56
diffuse, 14-04
factor, 5-15
law, 14-03
losses, 5-16
of pulse in distance measurement, 9-10
Reflectivity, acoustic, 12-40
Reflectors of antennas, 6-78
Reflex klystrons, 4-54
tubes, external cavity type, 4-57
Reflex tubes, internal cavity type, 4-57
Refraction, 14-02
at spherical surfaces, 14-05
dispersion, 14-05
index, 5-53
law, 14-02
sound, 12-60
Refrax, properties, 2-10
Regeneration in multistage amplifiers of tuned
r-f receivers, 7-118
Regenerative receivers, 7-117
objection to, 7-117
oscillation, 7-117
Register ton, conversion factors, 1-50
Regulators, voltage, 4-08
Relative capacity, symbol, 1-72
permeability, cgs unit, 1-46
mks unit, 1-46
symbol, 1-46
Relaxation circuits, 9-17
blocking oscillator, 9-18
flip-flop circuit stable in either condition,
9-17
free-running multivibrator, 9-18
triggered multivibrator, 9-18
oscillation, 7-84
Reluctance, magnetic, cgs unit, 1-46
mks unit, 1-46
symbol, 1-46
symbol, 1-73
Reluctivity, symbol, 1-73
Remalloy, 2-66, 2-67
Remote cutoff tube, 4-25
Repeater, 7-13
Repeller, 4-54
Repetition test, 12-28
Reproducing of sounds, 13-37
Reproduction systems, 16-02
Residual induction, defined, 2-60
Resimene, 2-39, 2-43
Resinox, 2-43
Resins, acrylic, 2-34
alkyd, 2-34
allyl, 2-34
Resistance, acoustic, 13-02
arc, 2-24
capacitance coupling, 7-04
-coupled audio amplifier of receivers, 7-125
coupling, 6-07, 6-08, 6-09
electrical, cgs unit, 1-46
conversion table, 1-61
mks unit, 1-46
symbol, 1-46
electrode, 4-11
equivalent negative, 7-28
equivalent-noise, 4-21
grid, 4-11
insulation, 2-23
lamps, 3-22
loads, 5-42
measurement, 11-23
measurements of, audio-frequency transform-
ers, 6-25
minimum, 5-08
mutual r., symbol, 1-73
plate, 4-11
radiation, 6-68, 13-02
self r., symbol, 1-73
stabilization in tuned r-f receivers, 7-118
standard, 11-18
decade, 11-20
symbol, 1-73
-temperature coefficient, symbol, 1-73
Resistivity, defined, 2-02
INDEX
41
Resistivity, earth, 10-32
electrical, cgs unit, 1-46
conversion table, 1-61
mks unit, 1-46
symbol, 1-46
surface, 2-23
symbol, 1-73
thermal, conversion table, 1-65
units, defined, 2-02
volume, 2-23
Resistoflex, 2-43
Resistors, 3-02
adjustable or variable, graphical symbol, 1-76
classifications, 3-04
dose-tolerance, 3-06
color code, 3-12
composition carbon, 3-11
defined, 3-02
deposited-carbon, 3-15
energy dissipation, 3-03
fixed resistance, 3-11
flat-type, 3-09
flexible, 3-09
frequency characteristic, 3-03, 3-14
graphical symbol, 1-76
in printed circuits, 3-22
low-power, 3-07
metal film, 3-17
non-ohmic, 3-23
pad-type, 3-09
physical and electrical considerations, 3-02
plug-in typo, 3-09
power ratings, 3-03
power-type, 3-05
layer windings, 3-07
non-inductive windings, 3-07
precision-type, 3-07
resistance tolerance, 3-03
resistance value, 3-02
special-purpose, 3-21
specifications, 3-05
spool type, 3-09
stability with age, temperature, and humidity,
3-04 ,
temperature rise, 3-03
tests, 3-05
thermal, typical characteristics, 11-77
winding typos, 3-09, 11-19
wire-wound, 3-05
Resolution, television, 20-02, 20-06, 20-66
Resonance, 5-30, 6-02
analyzers, 11-58
effect of, 12-33
frequency formulas, 11-03
frequency motor, 11-11
measurements, 11-27
room, 12-45
Resonant antennas, 6-81
circuits, 6-02
magnetron, graphical symbol, 1-78
-V antennas, 6-83
Resonators, 4-42
cavity, tfae Cavity resonators
quartz, 11-12
unsealed, humidity changes, 11-88
Respiration, artificial, 23-18
Respiratory muscles, speech and, 12-19
Restaurants, noise levels acceptable in, 12-58
Restrictions for physical readability, 5-11
Resuscitation, 23-18
Retina, of oyoa, 14-25
Retrace, television, 20-06
Return of pulse in distance measurement, 9-10
Reverberation, 12-40
Reverberation, at different frequencies, 12-47
combined effects of loudness and, 12-74
effect on hearing of speech, 12-73
equations, 12-43
formula, modification of, 12-43
free decay of modes of vibration and, 12-45
in auditoriums, 12-73
in coupled spaces, 12-46
measurement, 12-48
percentage articulation for various size rooms
and different times of, 12-74
room, effect on articulation, 12-38
time, 12-40, 12-43, 12-44, 12-45, 16-03
optimal, 12-75, 16-03, 16-11
Reversible permeability, defined, 2-60
Revolutions (circumferences), conversion table,
1-51
Revolutions per minute, abbreviation, 1-72
per second, abbreviation, 1-72
R-f amplifiers, 7-22
circuits, effect of, on fidelity curve of receivers,
7-125
gain and bandwidth, 11-53
signal, 20-17
Rheostats, 3-02, 3-17
defined, 3-02
physical and electrical considerations, 3-02
power-type, 3-19
wire-wound, 3-18
Rheotan, properties, 2-08
Rhodium, properties, 2-08
Rhombic antennas, 6-64, 6-83
Ribbon microphone, 13-23
speaker, 13-11
Rice system for neutralization, 7-29
Richardson's temperature law, 4-09
Rickets, 23-08
Rieke diagram, 4-49, 4-56
Right circular cone, mensuration, 1-18
circular cylinder, mensuration, 1-18
cylinders, modes in, mode-shape factor, 7-101
pyramid, mensuration, 1-18
rectangular cylinder cavity resonator, 7-96,
7-99, 7-101
Rigid partition, 12-65
Ripple frequency, 7-109
Rise time of input pulse in amplifiers, 9-14
Rising sun anode block, 4-42
RMA color code, 3-12
preferred numbers, 3-12
Rochelle salt, 13-56
properties, 13-65
use in oscillators, 7-92
use in piezoelectric crystals, 13-56
useful cuts, 13-67
Rocket antennas, 6-85
Rod, conversion factors, 1-47
square, conversion factors, 1-48
Roebling gage, 1-69
Roentgen therapy, apparatus, 23-12
van de Graaff generator, 23-12
general technical requirements, 23-12
purpose, 23-12
technique, 23-13
Roentgenography, apparatus, 23-15
general technical requirements, 23-14
industrial, tubes, 4-89
medical, tubes, 4-86
purpose, 23-14
technique, 23-14
Roentgenoscopy, apparatus, 23-15
general technical requirements, 23-14
purpose, 23-14
technique, 23-14
42
INDEX
Roentgenoscopy tubes, 4-86
Roods, conversion factors, 1-48
Rooms, acoustic properties, 12-39
banking, noise level acceptable in, 12-58
conference, noise levels acceptable in, 12-58
growth and decay of sound, 12-42
lecture, 12-42
live, reverberation equations and, 12-43
music, see Music rooms
normal frequencies for acoustics, 12-45
percentage articulation, 12-69
resonance, 12-45
resonant frequencies for acoustics, 12-45
speech power of speakers in various sizes, 12-73
Root-mean-square, 1-74
abbreviation, 1-72
Ropes, conversion factors, 1-47
Rose's metal, properties, 2-08
Rosin, 2-43
oil, dielectric properties, 2-50
properties, 2-28
Rotary joints of wave guides, 10-26
Rotational frequency, symbol, 1-73
Rotative operators, symbols, 1-73
R-63 alloy, properties, 2-08
Rubber, cyclicized, 2-43
hard, 2-43
power factor at high frequencies, 2-34
properties, 2-28, 2-30
sponge, compliance and resistance data in insu-
lation, of vibration, 12-62
synthetic, properties, 2-30
vulcanized, 2-44
Rubidium, properties, 2-08
Rug, 12-54
Rutile, 2-45
Sabin of acoustic properties of rooms, 12-40
Saflex, 2-45T 2-47
Saran, 2-45, 2-47
properties, 2-30
Saturable reactors, 3-48
Saturated sleeving, 2-45
Saturation induction, defined, 2-60
permeameter, 2-74
Saxophone, 12-25, 12-30
Scala media of ear, 12-03
tympani of ear, 12-03
vesitibuli of ear, 12-03
Scales, temperature, 1-43
conversion table, 1-64
Scaling, magnetrons, 4-45
Scalloping, denned, 22-06
Scanning, 20-03
circuits, for cathode-ray devices, 20-08
for electrostatic deflection, 20-08
horizontal resolution, 20-04
interlaced, 20-05
keystone correction, 20-11
magnetic, circuits, 20-10
output amplifiers, 20-61
mechanical, 20-07
method of microwaves in direction finding,
6-87, 6-88
vertical resolution, 20-04
Schematic eye, 14-28
Schering bridge, 11-26
Schools, address systems, 16-18
sound insulation, 12-57
Scophony, 20-08
Scotch tape, 2-45
Scotophors, characteristics, 15-37
defined, 15-32
mechanisms, 15-36
Screen-grid, defined, 4-04
lead inductance, 4-17
tubes, 4-03, 6-11
Screens, cathode-ray-tube, 15-37
intensifying, 23-15
luminescent, see Luminescent screens
Scruples, conversion factors, 1-55
Sealed tube, defined, 4-75
Secant, 1-07
abbreviation, 1-72
hyperbolic, 1-10, 1-26
Sech, WO, 1-26
Second (time), abbreviation, 1-72
standard, 1-43
Second (angular measure), abbreviation, 1-72
Second harmonic distortion, 4-24
in f-m systems, 8-28
Secondary daytime coverage, 16-32
emission, defined, 4-05
night-time coverage, 16-32
radiation, 23-15
service, 16-32
Seconds (angle), conversion table, 1-51
Seconds (time), conversion table, 1-51
Section of land, conversion factors, 1-48
Sectionally wound coils, use in i-f amplifiers, 7-58
Selectance, 7-115
Selective fading, multipath transmission and,
8-29
Selectivity, determination, in superheterodyne re-
ceivers, 7-56
in coupled circuits, 6-10
Selectron, 2-39
Self-admittance, 5-06
Self-excited oscillator, 4-49
Self-impedances, 6-07
Self-inductance, symbol, 1-73
Self-oscillation, conditions, 7-84
Self-reactances, in coupled circuits, 6-07
Self-resistances, in coupled circuits, 6-07
Semiabsolute system, 1-45
Semi-butterfly circuit, 3-57
Semicircular canal of ear, 12-02
plate forms, 3-57
Semi-remote cutoff tube, 4-26
Semi-tone, 11-09
Sendust, 2-62
Sensation area, auditory, 12-08
unit, 1-38
Sensitivity, determination, in superheterodyne
receivers, 7-56
ear, 12-08
Sequential television, 20-65
Series expansion, for plate current of a triode,
5-41
mathematical, 1-17
plate circuit, 5-41
power, 5-38
resonant circuits, 6-02
Taylor's, 1-17, 5-38
trigonometric, 5-39
-type networks, 6-35, 6-36
Service broadcast range, 10-47, 16-32
Shape of room, effect of, 12-69
Sharpness, 20-02
roentgenographic, 23-14
Sheet metal gages, 1-66
Shellac, 2-45
properties, 2-30
Shield, within envelope, graphical symbol, 1-78
Shielded loop antennas, 6-87
Shielding cans, input and interstage transformers
and, 6-21
large, use in i-f amplifiers, 7-58
INDEX
43
Shielding, problems, 11-101
Shin, 1-10, 1-26
Shipping measure, conversion factors 1-50
ton, 1-50
Shock, acoustic, 10-92
electric, 23-17
Shock therapy, 23-02, 23-04
Shockproof x-ray diffraction tube, 4-89
Short ton, conversion factors, 1-54
wave, 10-40
-wave antennas, locations, 6-75
sets, 7-60
Shot effect, 4-20
Shunt-fed antenna, 6-81
neutralization employed in power amplifiers
7-132
peaked amplifiers, 7-33
circuit, 7-33
inductance in terms of frequency and plate
load, 7-34
plate load in terms of frequency, 7-33
Side responses, reduction of, in f-m distortion,
8-29
Sideband analysis-synthesis method, for evaluat-
ing f-m distortion, 8-27
Sidebands of carrier frequency, in process of
modulation, 7-70
Side-tuned circuits as frequency detectors, 8-21
Siemens, mho, 1-46
Signal generators, 11-30, 11-89
amplitude modulation, 11-93
frequency modulation, 11-94
noise measurement, 11-44
pulse modulation, 11-95
-to-intorforence ratio in f-m systems, 8-30
tranaadmittance, 4-55
Signaling, use of pulses, 9-02
Signals, Naval Observatory time, 18-40
selection in frequency or time, 9-02
telegraph, 18-05
Silaneal, 2-45
Silastic, 2-45
properties, 2-30
Silchrome, properties, 2-08
Silfrax B, properties, 2-11
Silica, fused, 2-45
Silicon, 2-45, 2-53
-iron alloys, 2-61
powder, properties, 2-11
properties, 2-08, 2-11
Silicone fluid, properties, 2-30
dielectric properties, 2-50
glass laminate, properties, 2-30
rubber, properties, 2-30
sealing compound, properties, 2-30
varnish, properties, 2-30
varnished glass cloth, properties, 2-30
Sillc, 2-40
Silmanal, 2-68
Silver chloride, properties, 2-11
electrochemical equivalent, 1-79
properties, 2-08, 2-11
Simple raster, 20-03
aeries circuit, variation of current with fre-
quency, 6-03
variation of voltage components with fre-
quency, 6-03
Simultaneous equations, 1-03
linear, 1-04
Sine, 1-07
abbreviation, 1-72
anti-hyperbolic, 1-10
hyperbolic, 1-10
abbreviation, 1-71
Sine, hyperbolic, inverse, 1-10
Single-anode tube, defined, 4-75
-frequency modulation, 8-02
-frequency tone (sounds), 12-14
-mesh circuits, 5-02, 5-03, see oho Circuits,
single-mesh
Sinh, 1-10, 1-26
Sink, frequency, 4-56
margin, 4-56
Sinusoid, equation, 1-05
Sisal hemp, 2-46
Skin effect, 3-04, 11-18
eruptions, 23-08
Skip distance, 10-41
transmission, f-m distortion and, 8-29
Sky wave, see Wave propagation, sky wave
Slate, properties, 2-30
Slide-wire rheostat, 11-19
Slip, symbol, 1-73
Slope filters, f-m receivers and, 8-19
time, 5-35
Small deviation ratio, in f-m distortion, 8-27
Smith chart, 4-56
Snell's law, 14-02
Sodium chloride, properties, 2-11
properties, 2-08
Soft x-rays, 4-82
Soil, effect of, on directivity of antennas, 6-74
Solar day, 1-43
disturbances, 10-46
Solid angle, conversion table, 1-51
minimum resolvable, 20-02
anode magnetron, 4-40
Solids, dielectric absorption, 2-23
dielectric strength, 2-23
Sonne, 22-31
Sound absorption, coefficients, 12-50
of audience, individual persons and other
objects, 12-55
of hair felt in different laboratories, 12-56
of thicknesses of hair felt, 12-56
practical considerations of materials, 12-57
-absorptive coefficients of materials, 12-48
carrier, 20-20
chamber, 13-07
film, distortion, 12-35
foci, 12-70
insulation, 12-57
by rigid partitions, 12-63
ceiling isolator used in, 12-60
connectors used in, 12-60
considerations in selection of building mate-
rials and types of structure for, 12-67
flexible cushions used in, 12-60, 12-61
floor chair used in, 12-60
method for insulation of vibration, 12-61
principles, 12-60
supports used in, 12-60, 12-61
transmission coefficient for masonry or con-
crete, 12-63
types of structures recommended, 12-68
intensity, relation between nerve discharge rate
for a 1050-cycle tone and, 12-04
sensitivity of ear and, 12-05
recording, 16-19
-reinforcing systems, 16-14
indoor, 16-15
outdoor, 16-15
-reproduction systems, 16-02
studios, 16-02
noise levels, 16-04
reverberation time, 16-03
sound decay rate, 16-04
systems, audio amplifiers, 16-06
44
INDEX
Sound systems, audio facilities, 16-02
control equipment, 16-06
transmission, coefficients, 12-64
reduction factors, 12-65, 12-66
velocity of, 13-02
Soundhead, 16-22 i
Sounds, see also Acoustics
absorption in air of rooms and, 12-42
articulation, 12-27
auditory perspective, 12-39
common speech, characteristics, 12-20
growth and decay of, in rooms, 12-42
impact, conduction of, 12-60
individual sound articulation, 12-27
iso-masking intensity, 12-1 1
judgments of half pitch, 12-16
localization, 12-18, 16-02
loudness, 12-11, 12-14, 16-13
auditory magnitude, 12-11
computation for, with continuous energy
spectrums, 12-13
defined, 12-11
neural pulses and, 12-11
sone density, 12-13
sone of auditory magnitude, 12-11
loudness of levels, 12-11
loudness vs. loudness level, 12-12
loudness-level contours, 12-15
magnitude of subjective harmonics and, 12-15
masking contours for steady noise, 12-11
masking effects of, 12-11
masking spectrums, 12-11
of single-frequency tone, 12-15
perspective, 16-02
power, 16-18
pressure, 16-04
projection, 16-21
recording, 16-19
reflection from domed ceiling, 12-70
relative occurrence in telephone conversation,
12-20, 12-21
single-frequency tone, 12-14
stimulation patterns, 12-15
sound articulation, 12-27
spectrums of, in speech, 12-20
speech, characteristics, 12-20
damping constants, 12-20
low-frequency modulation, 12-20
steady, pitch, 12-16
syllable articulation, 12-27
transmission of, through ventilating ducts,
12-61
vowel articulation, 12-27
vowel-like, of speech, 12-20
Space capacitivity, cgs unit, 1-46
mlcs unit, 1-46
symbol, 1-46
charge, 4-02
-charge cloud, 4-41
-charge grid, defined, 4-04
permeability, 1-44
cgs unit, 1-46
mks unit, 1-46
symbol, 1-46
sense, 14-39
direction localization, 14-39
transmission, 10-29
Span, conversion factors, 1-47
Spark gap, plain, graphical symbol, 1-76
oscillator, 7-94
quenched, symbol, 1-76
rotary, 1-76
Sparkover, 2-54
voltages for sphere gaps, 2-55
Spauldite, 4-46
Speakers, condenser, 13-16
direct radiator, 13-11
enclosures, 13-13
dynamic, 13-11
horn-type moving-coil, 13-14
loud, 13-07
magnetic, 13-11
balanced-armature, 13-15
magnetic-armature, 13-15
bipolar, 13-16
moving-conductor, 13-11
pneumatic, 13-17
Special-purpose resistors, 3-21
Specific gravity, abbreviation, 1-72
heat, abbreviation, 1-72
conversion table, 1-64
inductive capacity, electrical, cgs unit, 1-46
mks unit, 1-46
symbol, 1-46
Spectrographs, 11-65
sound, 11-68
Spectrum analyzers, 5-28
electrical, 11-14
noise, 11-64
of sounds in speech, 12-20
Speech, see also Acoustics; Sounds; Speech power
analysis, 12-23
and music, 12-19
articulation test, 12-27
audible effects of phase distortion, 12-37
audible frequency range, 12-30
average power of speakers in various sizes of
rooms, 12-73
characteristics of sounds, 12-20
conversational, speech pressure vs. frequency
range, 12-22
description of organs, 12-19
effects of distortion, 12-29
hearing of, effect of noise, 12-72
effect of reverberation, 12-73
in auditoriums, 12-69
inflection, 12-20
input equipment, 12-02
larynx and, 12-19
levels of, average, for speakers in various sizes
of rooms, 12-73
ratio of noise to, 12-72
lungs and, 12-19
mechanism, 12-19
breath steam as, 12-19
friction modulation, 12-19
modulation, 12-19
vocal-cord modulation, 12-19
mouth cavities and, 12-19
nose cavities and, 12-19
optimal reverberation times for, 12-75
at different frequencies, 12-75
pharynx and characteristics of sounds, 12-20
power, 12-22
frequency distribution, 12-24
phonetic powers of 1 watt, 12-24
pressure measurement of mouth as radiator,
12-22
• powers, data on, 12-23
pressures, 11-60
production, 12-19
respiratory muscles and, 12-19
spectrum, 12-23
stress, 12-20
tests, 12-27, 12-28
laboratory, 12-27
throat cavities and, 12-19
trachea and, 12-19
INDEX
45
Speech, transmission, 12-27
vibrato, 12-20
visible, 12-21
cavity modulation, 12-21
fill, 12-21
frietional modulation, 12-21
patterns, 12-22
phonetic printing and, 12-21
plosive release, 12-21
start-stop modulation, 12-21
stop gap, 12-21
vocal resonance bars, 12-21
voice bar modulation, 12-21
visual, 12-21
vocal cords in, glottis, 12-19
vooal resonances, 12-20
vocoder used in, 12-21
voder used in artificial, 12-21
vowels, 12-20
wave forms, 12-22
average, 12-22
instantaneous , 12-22
peak, 12-22
types denned, 12-22
windpipe and, 12-19
Speed of information, 5-28
frequency bandwidths required for, 9-04
pulses and, 9-03
of rotation, 1-73
Spheres, conversion table, 1-51
mensuration, 1-18
Spherical candlepower, abbreviation, 1-72
optics of antennas, 6-77
right angles, conversion table, 1-51
Sponge rubber, 12-62
Spot, scanning, 20-04
Square, abbreviation, 1-72
centimeters, abbreviation, 1-72
conversion table, 1-48
conversion factors, 1-48
cross bracket, 5-43
factors, conversion factors, 1-48
foot, abbreviation, 1-72
conversion table, 1-48
pounds per, abbreviation, 1-72
inch, abbreviation, 1-72
conversion table, 1-48
pounds per, abbreviation, 1-72
kilometer, abbreviation, 1-72
kilometers, conversion table, 1-48
-law detection, 7-76, 7-78
defined, 7-76
-law detectors, detection of carriers and, 7-76
single sideband signals and, 7-7ft
motor, abbreviation, 1-72
conversion table, 1-48
micron, abbreviation, 1-72
mile, conversion table, 1-48
millimeter, conversion table, 1-48
myriameter, conversion factors, 1-48
pulses, widening of, by reduction of frequency
bandwidth, 9-04
rod, conversion factors, 1-48
root of mean square, abbreviation, 1-72
wave testing, 11-39
yard, conversion table, 1-48
Squares, theory of least, 1-15
Stability, frequency, 7-92
Stabilization, receiver, 7-118
Stacking of arrays, antennas and, 6-73
Stadium, address system, 16-15
Stage, amplifier, 7-04
sound, 12-02
Staggered tuning of coupled resonant circuits,
6-10
Stagger-tuned single-tuned circuits of amplifiers,
7-64
Stainless type 304, properties, 2-08
Standard broadcasting, 16-30
coverage, 16-32
capacitance, 11-20
time, 11-04
Wire Gage, 1-69
Standards, abbreviation, 1-72
of fundamental units, 1-42
television, 20-20
Standing-wave detectors, 11-72
waves, uniform lines, 5-25
Starting voltage, 4-08
Start-stop modulation in speech, 12-19, 12-20
Stat, 1-43
Statamperes, conversion factors, 1-59
Statcoulombs, 1-43
conversion factors, 1-58, 1-59
Statfarads, 1-43
conversion factors, 1-62
Stathenrys, conversion factors, 1-63
Static-characteristic measuring circuit, 4-08
plate resistance, 5-42
Statohms, conversion factors, 1-61
Statute miles, conversion factors, 1-47
Statvolts, conversion factors, 1-60
Steady-state velocity, 5-36
Steatite, 2-46
ceramics, properties, 2-30
power factor at high frequencies, 2-34
Steel wire, copper-clad, 2-20
gage, 1-70
tables, 2-19, 2-20
Steels, carbon, 2-66
Stefan-Boltzmann constant, 1-79
law, 4-09, 15-30
Steinmetz' law, 2-69
Steradians, conversion table, 1-51
Sterba array antennas, 6-65, 6-82
Stere, 1-49
Stereoscopic vision, 14-46
Stethophone, 23-11
Stilb, 1-46
Stimulation density, 12-12
Stirling's formula, 1-03
Stl, W. G., 1-69
Stone, conversion factors, 1-54
perch of, conversion factors, 1-49
Stop consonants of speech, 12-20
gap in visible speech, 12-21
Stops, optical system, 14-13
Stores, noise levels acceptable in, 12-58
Storms, magnetic, 10-46
Straight line, equation, 1-05
frequency, 3-58
wavelength, 3-58
Stranded wire, 1-66
Stratoscope, 22-31
Stray capacitance, 3-56
Stray electron currents, 4-11
Strength, dielectric, of gases, 2-54
of liquids, 2-51
of solids, 2-23
Stress, effect on magnetostriction, 2-70
in speech, 12-20
String galvanometer, 23-09
Stroboscopic method, used in frequency measure-
ment, 11-07
Strobotron tubes, 4-74
Strontium, properties, 2-08
titanate, properties, 2-30
46
INDEX
Strowger system, 17-10
connector, 17-13
director system, 17-15
impulse repeater, 17-12
intermediate distributing frame (IDF), 17-15
line finder switch, 17-11
main distributing frame (MDF), 17-15
plunger line switch, 17-10
rotary line switch, 17-11
secondary line switch, 17-11
selector, 17-13
toll switch train, 17-15
Struck bushel, conversion factors, 1-50
Structural coordination, 10-68
Structures, types recommended for sound insula-
tion, 12-68
Stubs' Iron Wire Gage, 1-66, 1-69
Steel Wire Gage, 1-69, 1-70
Stucco, 12-55
Studios, see also Broadcasting studios ; Recording
studios; Sound studios
motion picture, 12-54
small, noise-reduction factor, 12-69
television, 12-58
Studio-transmitter link, utilization of frequency
modulation, 8-02
Styraloy, 2-46
properties, 2-30
Styramic, 2-46
HT, 2-46
properties, 2-30
properties, 2-30
Styrene, 2-46
Styrofoam, 2-46
Styron, 2-42, 2-46
STJ, 1-38
Sub coupling, 6-09
Subharmonic synchronization, 7-88
Submarine cable telegraphy, 18-40
data, 18-41
operation, 18-42
Subscriber stations, 17-106
equipment, 17-106
protection, 17-113
telephone set, 17-106
dials, 17-110
housings, 17-110
receiver, 17-107
ringing circuit of, 17-109
services, 17-111
transmitter, 17-106
Substitution methods, 11-27
Successive approximations, 5-45
Sufficient coupling, 6-09
Sulfur, properties, 2-30
Sun lamp, 23-07
Sunspots, effect of, 10-46
Super-coupling, 6-09
Superheterodyne receiver, all-wave, 7-123
combined first detector and oscillator, 7-119
diode pentode tube, 7-121
fidelity determination, 7-56
frequency converter, 7-119
harmonics of the intermediate frequency, 7-122
i-f amplifier, 7-121
image response, 7-122
oscillator tracking, 7-121
preselector, 7-119
selectivity determination, 7-56
sensitivity determination, 7-56
six-tube, 7-120
tracking, 7-121
undesired responses, 7-122
Superior, properties, 2r08
Supermalloy, 2-62
Superposition, principle, 5-02
theorem, 5-34
Superregneration in receivers, 7-117, 7-118
Supports in sound insulation, 12-60, 12-61
Suppressor grid, defined, 4-04
pentodes, 4-03
input, screen output amplifiers, 7-51
noise, 7-126
Surface resistivity, 2-23
Surgery, high-frequency, 5-08, 23-06
Susceptance, minimum, 5-08
symbol, 1-73
Susceptibility, dielectric a., symbol, 1-73
magnetic s., symbol, 1-73
symbols, 1-73
Sweep frequency heterodyne, 11-66
SWG, 1-69
Swinging choke, 3-48
Switchboards, common-battery, 17-05
magneto, 17-03
manual toll, 17-36
mechanical toll, 17-36
multioffice multiple common-battery, 17-08
multiple common-battery, 17-07
single-office common-battery, 17-07
single-section common-battery non-multiple,
17-06
Syllable articulation, 12-27
Symbols, Greek alphabet, 1-79
letter, for magnitudes of electrical quantities,
1-72
standard graphical, 1-76
Symmetrical band-pass filter sections, design in-
formation, 6-44, 6-45, 6-46, 6-47
filter, image transfer function, 6-56
high-pass filter sections, 6-43
lattice, configuration of, filters and, 6-41
conversion of, filters and, 6-42
low-pass filter sections, 6-43
networks, 5-23
current and voltage relations, 5-23
impedance relations, 5-23
incident and reflected waves, 5-23
tandem combination, 5-23
sections, elementary structures forming com-
posite filters, 6-48
of filters, 6-41
Symmetry factor, 5-15
Synchronization of oscillators, 7-88
television, 20-17
Synchronous clock, 11-04
single-tuned circuits of amplifiers, 7-64
Synchroscope, used for pulse-measurements, 9-12
Synthane, 2-46
Synthetic insulating liquids, 2-52
rubber, 2-30
Syphilis, 23-06
Systems of units, 1-42
X and IT networks, 5-13
T section attenuator in single-mesh circuits, 6-06
Talk-back equipment, 16-10
Tan, 1-07, 1-21
Tandem telephone system, 17-49
crossbar equipment, 17-50
operation, 17-49
Tangent, 1-07, 1-21
abbreviation, 1-72
hyperbolic, 1-10
abbreviation, 1-71
Tangential resonance magnetrons, 4-42 fn.
Tank, 1-10, 1-26
Tantalum, properties, 2-08, 2-11
INDEX
47
Target, x-ray, graphical symbol, 1-78
Tarnac, properties, 2-08
Taylor's formula, 5-40
scries, 1-17, 5-38, 5-57
Tchebycheff type characteristics of filter design,
6-56
Techniques, pulse, 9-02
Teflon, 2-42, 2-46
Tegit, 2-46
properties, 2-30
Teleautograph system, 18-39
Teledeltos, 18-38
Telefax, 18-30
service, 18-38
Telegraph codes, 18-02
equipment, for central offices, 18-46
intermediate distributing frames, 18-47
multiplex distributors, 18-48
protector frames, 18-47
tape perforator, 18-48
telegraph repeaters, 18-47
teletypewriter switchboards, 18-47
testboards, 18-47
transmitter, 18-50
transmitter-distributor, 18-50
typing reperforator, 18-50
for stations, 18-51
printers, 18-52
radio-interference-suppression apparatus
(filters), 18-52
selectors, 18-52
signals, 18-05
systems, 18-02, 18-18
a-c, 18-35
specific telegraph level (STL), 18-35
automatic, 18-26
intercommunicating, 18-34
multiplex, 18-30
private line switching, 18-34
reperforator switching, 18-38
sub center switching, 18-33
varioplex, 18-31
clock circuits, 18*40
d-c, 18-18
composite arrangement, 18-18
duplex repeater, 18-26
duplex systems, 18-22
half duplex operation, 18-23
metallic circuit operation, 18-21
one-way polar circuit, 18-20
polarential operation, 18»20
quadruple* system, 18-25
simplex arrangement, 18-18
single lino repeater, 18-19
two-path polar operation, 18-20
upset duplex operation, 18-24
facsimile, 18-30
messenger call circuits, 18-39
miscellaneous, 18-38
Naval Observatory time signals, 18-40
radio, nee Radio telegraph
railroad communication, 18-40
teleautograph, 18-39
ticker, 18-38
transmitters, 7-134
Telegraphy, 18-02
a-c, 18-02
codes, 18-02
d-c, 18-02
distortion, 18-11
equipment, 18-40 m
signals, 18-05
submarine cable, 18-40
data, 18-41
Telegraphy, submarine cable, operation, 18-42
systems, 18-18
theory, 18-02
transmission methods, 18-02
wave shapes, 18-05
Telephone lines, cable, 10-04
subscriber, 17-69
toll, see Toll telephone lines
transmission consideration, 17-69
plant, exchange, see Exchange telephone plant
toll, see Toll telephone plant
receivers, 13-08, 13-17, 17-107
graphical symbol, 1-76
magnetic-armature, 13-18
moving-conductor, 13-17
piezoelectric, 13-18
simple, 5-65
repeaters, 17-39
set, subscriber, nee Subscriber telephone set
systems, auxiliary service equipment, 17-51
carrier, 17-43
central-office equipment, 17-03
common, 17-51
intermediate distributing frames, 17-51
main distributing frames, 17-51
protectors, 17-52
testboards, 17-52
crossbar, see Crossbar telephone system
McBerty automatic, 17-33
manual, 17-03
operation, 17-03
mechanical, 17-08
operation, 17-08
others, 17-33
panel dial, see Panel dial telephone system
power, 17-53
radio, see Radio telephone systems
rural power line carrier, 10-73
tandem, see Tandem telephone systems
toll, nee Toll telephone system
XY dial, 17-34
transmitter, 17-106
graphical symbol, 1-76
negative feedback and, 7-133
transpositions, 10-84
Telephony, 17-02
defined, 17-02
Teleprinter, 18-04, 18-26
Teleran, 22-29
Teletypesetting, 18-34
Teletypewriter, 18-04, 18-26
code, 18-04
distortion, 18-15
Exchange Service, 18-34
receiving mechanism, 18-27
regenerative repeater, 18-29
sending unit, 18-26
Television, 20-02
back porch, 20-16
beads, 20-04
binocular, 20-67
broadcasting, 20-g>
lens aperture required for, 20-21
camera, studio, design of, 20-22
Iconoscope, 20-23
Image Orthicon, 20-23
cathode-ray reproduction tubes, 15-46
color, compatibility, 20-66
methods of transmission, 20-65
physiological requirements, 20-66
receiver, 20-66
transmitter, 20-66
definition, 20-02
diplexing of picture and sound, 20-67
48
INDEX
Television, dot sequential, 20-65
equalizing pulses, 20-13, 20-17
facilities, intercity, 20-37
local, 20-39
field of view, 20-02
field pick-up equipment, 20-36
field sequential, 20-65
for special services, 20-67
front porch, 20-16
other forms of, 20-64
physiological requirements, 20-02
pick-up devices, aperture distortion, 20-30
film, 20-31
pick-up tubes, 15-19
requirements, 15-19
picture channel, i-f amplification, 20-49
second detector, 20-52
polarization, 20-20
principles and theory, 20-02
receivers, 20-46
antennas, 20-47
local oscillator, 20-49
modulator, 20-49
noise limiters, 20-55
picture gain control, 20-54
picture tube, 20-54
power supply, 20-62
r-f circuits, 20-47
scanning circuits, 20-59
scanning oscillator, 20-60
sound amplifiers, 20-56
synchronizing circuits, 20-57
reflective optical system for projection, 14-20
reproduction, 20-03
scanning, 20-05
signal, relay, 20-37
standards, 20-20
standards of foreign countries, 20-64
studio equipment, amplifier design, 20-27
control room, 20-26
delay networks, 20-29
master control, 20-32
monitoring and switching facilities, 20-27
time delay networks, 20-28
studios, noise levels acceptable in, 12-58
test pattern, 20-14
theater, 20-64
transmission, 20-03
composite signal, 20-16
pick-up devices, 20-07
pulse measurement, 20-33 -— —
r-f signal, 20-17
subdivision of pictures, 20-03
synchronizing signal, 20-1 1
video signal, d-o component, 20-13
transmitting plant, antennas, 20-46
d-c transmission, 20-43
equipment, 20-41
measurement of r-f output power, 20-45
modulated amplifier, 20-42
modulation measurement, 20-44
modulation method, 20-42
neutralization, 20-42
performance measurements, 20-46
r-f monitoring, 20-44
transmission line, 20-46
vestigial sideband transmission, 20-43
visual carrier frequency generation, 20-42
Tellurium, properties, 2-08
Temperature, 1-42, 1-46
abbreviation, 1-72
cgs unit, 1-46
coefficients, of copper, 2-03
of electric resistance, 2-02, 3-13, 3-16
Temperature, conversion formulas, 1-64
effect, on magnetization, 2-69
mks unit, 1-46
symbol, 1-46, 1-73
scaloH, 1-43
conversion table, 1-64
Tempered scale, 11-10
Tenebrescence, defined, 15-32
Tenebrescent materials, 15-29
Tenite I, 2-36, 2-4«
II, 2-30, 2-46
Tensile breaking load, for solid wires, 2-21
strength, conductor^ 2-04
for aolid wires, 2-21
Terms, engineering, abbreviations, 1-71
Terrain clearance indicator, 22-32
effect, on directivity of antennas, 6-74
Test pattern, television, 20-14
waves, 11-55
Tests, articulation, 12-31
of music transmission, 12-27, 12-28
of speech, 12-27, 12-28
Tetrode, characteristics, 4-34, 4-35, 4-36
defined, 4-04
detectors, 7-82
load rectification, 7-82
Textiles, glass, 2-38
TextoUte, 2-46
Thalid, 2-39, 2-46
Thallium, properties, 2-08
Thalofide, 15-11
Theaters, see also Auditoriums
noiae levels acceptable in, 12-58
projection, 16-13, 16-21
sound insulation, 12-57
Theory of least squares, 1-15
Therapy, Section 23
roentgen, 23-12
tubes for x-ray, 4-83
ultraviolet, 23-06
Therlo, properties, 2-08
Thermal-acoustic noise, 12-06
agitation, 4-20
conductivity, conversion table, 1-65
devices, bolometer, 15-04
radiometer, 15-04
thermoj unctions, 15-03
ohms, 1-65
radiation, 15-29
resistivity, conversion table, 1-65
units, British, conversion factors, 1-57, 1-C4,
1-65
Thermionic cathode, 4-02
emission, defined, 4-05
vacuum tubes, 4-02
Thermistor bolometer, 15-04
Thermistors, 3-02, 3-28
Thermocouple, 11-16
Thermoelement, graphical symbol, 1-76
Thermo junctions, 15-03
Thevenin's theorem for linear networks, 5-12
Thiokol, 2-44, 2-46
Third harmonic distortion, 4-24
in f-m systems, 8-28
Thousand, abbreviation, 1-72
Three-electrode cold-cathode tubes, 4-73
-winding transformers, 6-12
Threshold of feeling, 12-09
of hearing, 12-05
voltage, 4-44
tfhroat cavities, speech and, 12-19
microphone, 22-12
Thyratron contactors, 21-11
grid-control circuits, 21-19
INDEX
49
Thyratron modulators, 9-22
Thyratrons, 4-60
anodo current averaging time, 4-64
anode nurge current, 4-64
availablo typos, 4-61
average anode current, 4-63
coiJHtruetion, 4-60
control ohuraetoriHtioH, 4-65
critical anodo voltage, 4-65
critical grid voltage, 4-65
current limita, 4-63
deionization time, 4-67
grid current, 4-64, 4-66
hot-cathode, 4-71
peak anode current, 4-63
peak forward voltage, 4-62
peak invorna anode voltage, 4-62
pulHfl, 4-69
construction, 4-70
repetition rate of pulnoH determined by, 9-19
whitnld-grid characteristics, 4-66
voltage limits, 4-62
Thyrlte, 3-26
Ticker system, 18-38
Tickler coil, 7-128
Tico, properties, 2-08
Ticonal, 2-66
Time, 1-42, 1-46
eg« unit, 1-46
constant, wymbol, 1-73
convention table, 1-51
inkn unit, 1-46
of reverberation, 12-43
of ri«B, 5-35
wtandard of, 1-43
standard used in frequency measurement, 11-04
uymbol, 1-46, 1-73
Tin Plate Oage,, 1-66
proportion, 2-08, 2-11
Tissue, destruction of, 23-12
Titanium dioxide, properties, 2-30
TM«mode cavity, 11-92
Tolerance current, 23-04
Toll telephone Una*, 17-60
circuit line-up procedure, 17-77
circuit operating requiromentw, 17-71
general twitching plan, 17-70
Rorvitto requirements), 17-69
mgntiling, 17-78
terminal IOHH, 17*77
plant, cable facilities, 17-86
dcmgn, 17-82
op<3U»wira facilities, 17-82
system, 17-30
No. 4 crossbar, 17-37
optsration, 17-36
Toluene, dielectric properties, 2-50
Ton, British flipping, 1-50
conversion factors, 1-54
register, convermon factors, 1-50
U. 8. dipping, 1-50
Tone control of receiver circuits, 7-126
rango, 12-30
Tonnage, 1-50
Tophet, 2-08
Torque, cga unit, 1-46
convention table, 1-46
inks unit, 1-46
Hyinbol, 1-46
Total reflection, 5-54
Tourmaline, use in oncillators, 7-92
Tower antennas, 6-81
Trachea, upfiech and, 12-19
Track, defined, 22-05
Tracking of superheterodyne receivers, 7-121
Traffic noise, see Noise, traffic
Transadmittance, beam, 4-53
defined, 4-05
Transconductance, 4-12
beam, 4-53
conversion, defined, 4-06
defined, 4-05
measurement circuit, 4-12
of tubes, 6-11
Transducer, ideal, 5-15
loss, 5-15
Transfer admittance, 5-07
characteristic, 4-11, see also Gamma (transfer
characteristics)
defined, 4-06
constant theorem of filters, 6-39
impedance, 5-06, 5-10
power, see Power transfer
Transferred reactance, 6-08
resistance, 6-08
Transformer-coupled amplifiers, 7-05
input circuit calculations, 7-07
Transformers, air-core, 6-10
graphical symbol, 1-76
audio-frequency, 6-13
capacitance measurement, 6-25
capacitance to ground, 6-24
complete equivalent network, 6-14
core-loss resistance measurement, 6-25
distributed capacitance of winding, 6-24
efficiency, 6-16
equivalent direct-connected network and,
6-13
equivalent network at high frequencies, 6-16
frequency characteristic measurement, 6-25
inductance measurement, 6-25
leakage inductance, 6-23
low-frequency characteristics, 6-15
measurements, 6-25
physical design, 6-22
resistance measurement, 6-25
simplified network at low frequencies, 6-15
single network at middle frequencies, 6-16
turns ratio measurement, 6-25
driver, 6-22
distortion, 6-22
frequency response, 6-22
leakage reactance, 6-22
turns ratio, 6-22
winding arrangement of class B, 6-22
filament, 6-26
function, 6-13
impedance, for wave-guide component, 10-22
input, 6-13, 6-19
frequency characteristics, low and middle
frequencies, 6-20
leakage resonance, 6-21
made with two-legged core, 6-22
pick-up, 6-21
shielding, 6-21
turns ratio, 6-20
use of shielding cans and, 6-21
interstage, 6-13, 6-19
frequency characteristics, low and middle
frequencies, 6-20
leakage resonance, 6-21
pick-up, 6-21
shielding, 6-21
turns ratio, 6-20
use of shielding cans and, 6-21
iron-core, graphical symbol, 1-76
line, 6-13, 6-19
modulation, 6-13, 6-19
50
INDEX
Transformers, output, 6-13, 6-17
frequency response, 6-17
loudspeaker loads, 6-18
pushpull, 6-18
turns ratio, 6-17
plate, 6-26
power, 6-26
calculation of performance, 6-29
construction, 6-27
copper loss of windings, 6-29
core loss, 6-28, 6-29
design procedure, 6-28
efficiency of, denned, 6-30
flux density, 6-28
heating, 6-29
insulation, 6-29
regulation of secondary winding, 6-30
size, 6-26
pulse, see Pulse transformers
three-winding, 6-12
tuned r-f, employing compound coupling, 6-11
vibrator, buffer capacitor, 6-31
function, 6-30
with iron cores, 6-13
with variable coupling, graphical symbol, 1-76
Transient disturbances, 5-26
defined, 5-27
frequency spectrum, 5-28
Transients, energy integral, 5-35
Fourier integral, 5-27, 5-33
idealized filters, 5-35
in networks, 5-26
oscillatory, 5-27
periodic, 5-27
properties, 5-26
superposition theorem, 5-34
types, 5-27
Transit time of an electron, 4-15
Transite, 2-46
Transition loss, 5-15
units in coupling wave guides, 10-24
Transmission circuits, 10-02
frequency spectrum, 10-02
types of communication, 10-02
coefficients, 18-54
for various layers of hair felt, 12-63
crossfire, 18-54
equivalents, 1-38
table, 1-39
frequency, characteristic of coupled circuits,
6-09
gain, 11-33
high-frequency, 10-02
in space, 10-29
line Q, formula, 11-91
lines, 5-24, see also Wire transmission lines
calculations, 11-70
construction, 10-49
electrical protection, 10-58
elementary section, 5-24
exchange cable protection, 10-59
mechanical features, 10-49
phase characteristic, 11-35
toll cable protection, 10-61
used in frequency measurement, 11-13
loss, 11-30, 12-60
maintenance, 18-53
measurements, 11-32
modes of wave guides, 10-10
obstacles, 10-42
atmospheric interference, 10-42
fading, 10-45
solar disturbances, 10-46
of music, 12-27, 12-28
Transmission, picture, 9-06
radio, national and international regulations,
7-129
sound, 12-61
standards, 18-53
television, 20-03
unit, 1-37
Transmlssometer, 22-13
Transmitters, a-c power used for, 7-108
circuits for f-m, 8-15
emergency, 8-15
filament power, 7-109
filter design, 7-110
frequency modulation, see F-m transmitters
hum due to filament current, 7-109
picture, see Picture transmitters
plate power, 7-109
power supply, 7-108
radio, 7-129
a-m, 7-129
audio amplifiers, 7-134
circuit Q and, 7-130
frequency control, 7-219
harmonic amplifiers and, 7-130
installation, 7-134
interstage coupling circuits, 7-129
modulation characteristics measurements,
7-135
negative feedback and, 7-133
oscillator power, 7-129
power amplifiers and, 7-131
scope, 7-129
unmodulated intermediate amplifiers, 7-130
sites, a-m broadcasting stations, 16-29
f-m broadcasting stations, 16-30
telegraph, 7-134
telephone, filter, 7-112
graphical symbol, 1-76
negative feedback and, 7-133
types of rectifiers used in, 7-109
Transpositions, 10-78 to 10-85
Transrectification factor of detectors, 7-81
Trapezoid, mensuration, 1-17
Traveling-wave magetrons, 4-41
operation, 4-42
T-r-f receivers, see Tuned-r-f receivers
Triangle, mensuration, 1-17
musical, 12-25
Triggered multivibrator, 9-18
Trigonometric formulas, 1-07
functions, of an angle, 1-07
relations between hyperbolic functions and,
1-11
series, 5-38, 5-39
tables, 1-21
Trigonometry, 1-09
Triode-heptode with rigid envelope connection,
graphical symbol, 1-78
power amplifiers, 7-10
voltage amplifiers, 7-10
Triodes, 4-02, 4-03
approximate series expansion for plate current,
5-41
characteristic curves, 4-31, 4-32, 4-33
classification, 4-03
defined, 4-04
equivalent circuit, 4-07, 5-49
input impedance, 5-49
mutual characteristic, 5-41
with filamentary cathode, graphical symbol,
1-78
with load, characteristics, 5-42
Trombone, 12-25, 12-30
Troy weight, conversion factors, 1-54, 1-55
INDEX
51
Trumpet, 12-25, 12-30
TU, 1-38
Tuba, 12-25, 12-30
Tube 1635 as class B audio amplifiers, 7-19
Tubes, ballast, 4-08
baae terminate, 1-78
battery, used in combinations for amplifiers,
7-21
cathode-ray, see Cathodo-ray tubes
cold-cathode, 4-72
available types, 4-75
tent, 4-74
Orookofl, 4-58
double-cavity velocity-modulation, with col-
lecting electrode, graphical symbol, 1-77
electron, defined, 4-03
envelope terminals, 1-78
fluoroftoopy, 4-89
ga«, defined, 4-03
gaH-fillocl, 4-02
oscillations, 7-91
gaseous? conduction, 4-68
hard, of x-ray, 4-82
high-vacuum, 4-02
defined, 4-04
industrial roentgenography, 4-89
matching the impedance, 6-11
medical roen Iconography, 4-86
mercury pool, with excitor, control grid and
holding anorlo, graphical symbol, 1-77
with ignitor and control grid, graphical sym-
bol, 1-77
mercury- vapor, defined, 4-04
metal, 4-62
muHianode, defined, 4-75
multi-electrode, 5-45
multi-grid, 4-03
multiple-unit, defined, 4-04
mutual conductance, 6-11
nowo, 4-23
oscillograph, multiple gun, 16-47
Ofioillograph-typo cathode-ray, «e« Cathode-ray
tubODi oscillograph type
pentode type, 6-11
pick-up, application, 15-29
picture, ««« Picture tubes
pool, defined, 4-75
pool-cathode, 4-75
available, 4-76
clainification, 4-77
projection, defined, 16-46
pulno, 9-26
radial dof lection, 15-47
receiving, classification chart, 4-28
reflex, 4-54
external cavity type, 4-57
internal cavity type, 4-57
rocmtgononcopy, 4-86
remote cutoff, 4-25
•oreen-tfrid, 4-03, 6-H
sealed, defined, 4-75
jwmi-rarnote cutoff, 4-26
shookproof x-ray diffraction, 4-89
single-anode, defined, 4-75
Boft, of x-ray, 4-82
fttrobotron, 4-74
television cathode-ray reproduction, 15-46
television pick-up* «e« Television pick-up tubes
three-electrode cold-cathodo, 4-73
thyratron, «ee Thyratrona
transeonduetanee, 6-11
universal therapy, 4-84
vacuum, w& Vacuum tubes
voltage drop, defined, 4-05
Tubes, voltage-regulator, 4-08, 4-73
wide-band amplifier, figure of merit for, 7-43
x-ray, 4-81
classifications, 4-81
diffraction, 4-89
therapy, 4-83
uses, 4-83
Tubing, varnished, 2-47
Tuf-flex, 2-46
Tuned amplifier circuits, 6-11
amplifiers, 7-06
circuit analyzer, 11-58
coupling of amplifiers, 7-06
-grid oscillator, 7-84
-plate tuned-grid oscillators, 7-83
-reed analyzer, 1 1-65
-r-f receivers, 7-56, 7-118
employing screen-grid tubes, 7-119
neutralization use to eliminate oscillation,
7-119
resistance stabilized, 7-118
sources of regeneration, 7-119
r-f transformer, employing compound coupling,
6-11
transformer coupled amplifiers, 7-06
Tungsten, 4-03
properties, 2-08, 2-09, 2-11
thoriated, 4-03
Tuning, 4-50, 6-04
electronic, 4-55
-fork oscillators, 7-91
wand, defined, 11-49
Turns ratio, measurements of, audio-frequency
transformer, 6-25
of driver transformer, 6-22
of input transformer, 6-20
of interstage transformer, 6-20
of output transformer, 6-17
Turnstile antennas, 6-84
Turpentine, dielectric properties, 2-50
Turx, 2-38, 2-46
Twists of rectangular wave guides, 10-21, 10-22
Two-digit decade counter (computer) , 9-09
-frequency modulation, 8-07
-terminal impedances, 5-07
-terminal reactive networks, 6-35
-way telephony, 7-14
Tympani, 12-30
Typewriters, noise analysis and, 12-58
Ultra-high-frequency measurements, 11-11
transmission, 10-35
Ultraviolet radiation, apparatus, 23-06
medical uses, 23-06
therapeutic use, 23-07
Unbalanced response to a-m distortion and, 8-28
Un-by-passed cathode resistance, 4-19
resistor, 4-20
Underground conduit, 10-58
Unidirectional broadside arrays of antennas, 6-73
couplet of antennas, 6-73
Uniform spectrum of f-m interference, 8-30, 8-31
Unipotential cathode, 4-08
Unit impulse, 5-27
step, 5-27
United States pound avoirdupois, 1-42
Standard Gage, 1-66, 1-67
Steel Wire Gage, 1-69
yard, 1-42
Units, absolute, of electrical measure, 1-44
angstrom, conversion factors, 1-47
international, 1-79
British thermal, abbreviation, 1-71
conversion factors, 1-57, 1-64, 1-65
52
INDEX
Units, centigrade, 1-43
conversion table, 1-64
cgs electromagnetic, 1-46
electric, 1-43
practical, 1-44
electromechanical systems, 5-63
fahrenheit, 1-43
conversion table, 1-64
imaginary, 1-06
international, of electrical measure, 1-44
inks system, 1-42, 1-45, 1-46
of conductivity, defined, 2-02
of resistivity, defined, 2-02
sensation, 1-38
standards of fundamental, 1-42
systems, 1-42
transmission, 1-37
Universal joints of wave guides, 10-26, 10-28
resonance curve, 6-04
therapy tube, 4-84
winding of coil, 3-34
Univibrator, 9-18
Unsymmetrical sections of filters, 6-50
Unzoned lens of reflectors of antennas, 6-78
Upper limits of hearing, 12-08
Urea formaldehyde, properties, 2-30
resins, 2-46
Vacuum-tube circuit, elements, 7-02
oscillators, 7-83
beat frequency, 7-89
Colpitts circuit, 7-83
current and voltage relations in simple
oscillator circuits, 7-85
dynatron, 7-89
harmonic content, 7-88
Hartley circuit, 7-83
simple oscillator circuits, 7-83
voltmeters, defined, 11-17
tubes, a-c equivalent circuit, 4-07
amplifier stage considering low-frequency re-
sponse only, 7-45
applicable to wide-band amplifier service,
7-43
cascade amplifiers, 7-03
cathode current for long pulses, 9-26
characteristic curves, 4-31
circuit elements, 7-02
classifications, 4-03
definitions, 4-03
effect of the grid coupling capacitor-resistor,
7-45
effect of internal impedance of the power
supply, 7-46
effect of the screen by-pass, 7-46
figure of merit for wide-band amplifier, 7-43
input admittance, 4-15
interelectrode, capacity impedance of, 7-02
lighthouse, 7-89
methods of measuring tube currents, 4-08
noise generated, 4-20
operation, 4-14
principles, 4-02
performance calculations from tube con-
stants, 7-09
pulse circuits and, 9-26
thermionic, 4-02
van der Pol's equation, 7-85
Vanadium Permendur, 2-62
V-antennas, 6-64
Var, 1-46
Variable-gain pentode voltage amplifiers, 7-12
selectivity of i-f amplifiers, 7-59
Variation, capacitance, 5-41
Variation, hearing, with age, 12-08
inductance, 5-40
Varistors, 3-02, 3-22
copper-cuprous oxide, 3-23
silicon carbide, 3-26
Varley loop test, 11-42
Varnish, insulating, properties, 2-30
Varnished cloth, 2-47
properties, 2-30
tubing, 2-47
Varnishes, insulating, 2-46
Vectolite, 2-68
Vector, mechanicl impedance, 5-59
Poynting's, 5-51
Velocity, angular, cgs unit, 1-46
conversion table, 1-53
mks unit, 1-46
symbol, 1-46
cgs unit, 1-46
conversion tables, 1-52, 1-53
electron, 4-14
group, 5-36
linear, conversion table, 1-52
microphone, 13-23
mks unit, 1-46
modulation, 4-51
of light, 1-79
of phase propagation, 5-25
phase, 5-36
steady-state, 5-36
symbol, 1-46
Ventilators, 12-54
Versed sine, abbreviation, 1-72
Versine of x, 1-08
Vertical hyperbola, 1-05
parabola, 1-05
resolution, 20-04
synchronizing pulse, 20-17
separation indicator, 22-31
Vestigial sideband, 20-19
Vibrating reed, 5-62
frequency meter, 11-11
Vibration constant, symbol, 1-73
Vibrations, 5-56
modes of, room resonance and, 12-45
solid-borne, insulation of, 12-61
Vibrato in speech sounds, 12-20
Vibrator transformers, buffer capacitor, 6-31
design, 6-31
function, 6-30
Vibrins, 2-39, 2-47
Vicalloy, 2-67, 2-68
Victory siren, 12-58, 12-59
Video-frequency amplifier, 9-15
signal, 20-13
system, overall, response, 20-35
Viewing distance, 20-02
Vinyl chloride, 2-47
chloride-acetate, 2-48
properties, 2-30, 2-32
plastics, 2-47
properties, 2-30
resin, hard, power factor at high frequencies,
2-34
Vinylidene chloride, 2-48
properties, 2-32
Vinylite, 2-48
X, 2-47
Vinyon, 2-48
Violet-ray therapy, 23-06
Visible speech, see Speech, visible
Vision, 14-25
adaptation, 14-33
binocular, 14-46
INDEX
53
Vision, differential sensitivity, 14-32
perwHtency, 14-33
Hpectral luminosities, 14-31
stereoscopic, 14-46
throHhold of light visibility, 14-30
Vistanex, 2-48
Visual acuity, 14-40
illumination and, 14-42
hearing, 12-21
telephony, 12-21
Vitamin D, 23-07
Vitreosil, 2-48
Vocal cord«, 12-19
reaonanties, in speech, 12-20
Vocoder, 12-21
Voice, artificial, 12-21
bar modulation in visible speech, 12-21
Volt, abbreviation, 1-72
-ampere, abbreviation, 1-72
rating, of secondary winding of power trans-
formers, 0-26
reactive, abbreviation, 1-72
Voltage, amplification, 4-07
anode, defined, 4-06
peak (or crest) forward, defined, 4-05
peak (or crest) inverse, defined, 4-05
conversion factors, 1-60
critical, 4-40
cutoff, 4-40
formula, 4-40
filament, changes in, 4-26
defined, 4-05
grid, defined, 4-05
heater, changes in, 4-26
defined, 4-05
in coupled circuits, 6-07
induced in antennas, 6-69
limitera, 3-23
loops, 6-26
mottmirernont, 11-17
nod<w, 5-20
non-mnufloidal, 5-02
of antennas, 6-66
plato, defined, 4-05
ratio, logarithmic, 1-38
regulator tubes, 4-73
regulators, 4-08
threshold, 4-44
Voltmeters, 2-76
graphical symbol, 1-76
Voltron, 2-48
Volts, 1-44, 1-45, 1-46
conversion factors, 1-60
Volume, o&8 unit, 1-46
controls, manter, 16-09
mixer, 16-07
conversion table, 1-49
energy, figs unit, 1-46
mk« unit, 1-46
symbol, 3-46
indicator, 16-10
level, 1-41
m\w unit, 1-46
of perfect KM, 1-79
resistivity, 1-61, 2-23
symbol, 1-46
Vowel-like sounds of speech, 12-20
VS, 11-02
Vu, Ml
Vulcabeston, 2-48
Vulcold, 2-48
Vycor, 2-48
Wagner ground, 11-26
Walls, isolating treatment in sound insultion,
12-60
noise-reduction factor and, 12-69
Washburu and Moen gage, 1-69
Water, acoustic properties, 13-02
dielectric properties, 2-50
measuring flow, 1-52
relation between dielectric constant and 3
tivity, 2-51
Watt, 1-44
abbreviation, 1-72
conversion factors, 1-58
-hours, conversion factors, 1-57
-second, 1-44
conversion factors, 1-57
Wave analysis, 11-54, 11-58
antennas, 6-64
equation, 5-51
filters, electric, 6-33
general purpose, 6-33
-guide antennas, 6-64
-guide components, motional joints, 10-26
other, 10-28
transformers for, impedance, 10-22
-guide connectors, 10-19
choke-flange type couplings, 10-20, 10-21
contact couplings, 10-20
-guide output coupling, 4-47, 4-48
guides, 10-09
characteristics, 10-17, 10-18
circular, 10-13
components, 10-17
defined, 10-09
dielectric, defined, 10-09
discontinuities, 10-16
flexible, 10-18
group velocity, 10-10
metal, defined, 10-09
modes of transmission, 10-09
of arbitrary cross-section, 10-15
phase velocity, 10-10
propagation constants of ideal, 10-10
rectangular, 10-11
bends, twists, and angles, 10-21, 10-22
rubber-covered flexible assembly, 10-18
special characteristics, 10-15
normal, 5-53
propagation, 10-29
ground wave, 10-29, 10-31, 10-32
free-space transmission, 10-31
transmission, 10-32
ultra-ionospheric range, 10-35
sky wave, 10-29, 10-37
high frequencies (short waves) , 10-40
intermediate frequencies, 10-40
low frequencies (long waves), 10-39
Wavelength, 5-51
constant, symbol, 1-73
of paraboloid antenna, 6-76
of red cadmium line, 1-79
symbol, 1-73
Wavemeters, 11-85
calibration, 11-87
used in pulse measurements, 9-12
Waves, centimetric, 1-80
continuous, 9-02
comparison of pulsed waves and, 9-02
decametric, 1-80
decimetric, 1-80
diverse, in distance observation, 9-09
tiectometric, 1-80
incident, 5-53
symmetrical networks, 5-23
uniform lines, 5-25
54
INDEX
Waves, kilometric, 1-80
metric, 1-80
millimetric, 1-80
myriametric, 1-80
progressive plane, 5-51
pulsed, 9-02
comparison of continuous waves and, 9-02
reflected, 5-53
symmetrical networks, 5-23
uniform lines, 5-25
refracted, 5-53
standing, uniform lines, 5-25
Wax, 2-48
power factor at high frequencies, 2-34
Weber, 1-45, 1-46
conversion factors, 1-63
Weeks, conversion table, 1-51
Weight, abbreviation, 1-72
apothecaries', conversion table, 1-55
avoirdupois, conversion factors, 1-54, 1-55
conversion table, 1-54
gage, 1-66
Troy, conversion factors, 1-54
Weighted observations, 1-15
Weston frequency meter, 11-11
Wheatstone bridge circuit, 4-11
Whispering gallery, 12-70
White level, 20-13, 20-20
Whole tone, 11-09
Wide-band amplifiers, 7-31
alternative designs, 7-64
double-tuned circuits used in, 7-64
figure of merit, 7-64
figure of merit of tubes, 7-43
formulas, summary, 7-44
high-frequency compensation methods, 7-43
high-frequency response, 7-31
inverse-feedback amplifiers used, 7-64
low-frequency response, 7-44
Miller capacitance effect of tubes, 7-43
peaking coil distributed capacity, 7-40
rise time of pulses, 7-64
stagger-tuned amplifiers used in, 7-64
synchronously sing-tuned circuits used in,
7-64
video amplifier response curves, 7-42
with constant- K-type coupling network, 7-39
i-f amplifiers, feedback pair, 7-68, 7-69
feedback triple, 7-68, 7-69
Wien's displacement law, 15-30
Wiggles, defined, 22-06
Winchester bushel, 1-50
Wind pressure, 10-53
Windows, coefficients of sound transmission,
12-65
noise-reduction factor and, 12-69
Windpipe, speech and, 12-19
Wire, alloy, of high tensile strength, 2-21
aluminum (tables), 2-17, 2-18
copper (tables), 2-12, 2-13, 2-14, 2-15, 2-16
enamel, 2-36
equivalents for pole-line loading calculations,
10-52
Wire, gages, 1-66, 1-68, 1-69, 1-70, 2-12
comparison, 1-69, 1-70
diameters, 1-70
line measurement, 11-32
solid, tensile breaking load, 2-21
steel, copper-clad, 2-20
steel (tables), 2-19, 2-20
transmission lines, 10-02
cutoff frequency, 10-07
electrical characteristics, 10-02
equivalent networks, 10-08
propagation constant, 10-06
velocity of propagation of wavelength, 10-07
wavelength, 10-07
-wound resistors, 3-05
Wires, crossed, not joined, graphical symbol,
1-76
joined, graphical symbol, 1-76
Wood, cord of, conversion factors, 1-49
properties, 2-32
studs and plaster, coefficients of sound trans-
mission, 12-66
Wood's metal, properties, 2-09
Woodwork shop, noise analysis, example of, 12-58
Word intelligibility, 12-28
Work, cgs unit, 1-46
conversion table, 1-57
mks unit, 1-46
symbol, 1-46, 1-73
Woven winding, 11-19
Wrought iron gage, 1-67
X-ray burn, 23-18
diffraction, tubes, 4-89
shockproof , diffraction tube, 4-89
therapy, see Roentgen therapy
tubes, 4-83
tubes, 4-81
classifications, 4-81
uses, 4-83
XY dial telephone system, 17-34
Yankee silver, properties, 2-09
Yard, abbreviation, 1-72
British imperial, 1-42
conversion table, 1-47
cubic, abbreviation, 1-71
conversion table, 1-49
square, conversion table, 1-48
U. S., 1-42
Years, abbreviation, 1-72
conversion table, 1-51
Z marker, 22-10
Zero beat, 11-05, 11-09
hearing loss, 12-07
level, 1-41
Zinc oxide, properties, 2-11
properties, 2-09, 2-11
Zircon porcelain, 2-48
power factor at high frequencies, 2-34
properties, 2-32
ELECTRICAL ENGINEERS' HANDBOOK
ELECTRIC POWER
Fourth Edition
SECTION
1. MATHEMATICS, UNITS, AND SYMBOLS
2. PROPERTIES OF MATERIALS
3. ELECTRIC CIRCUITS AND ELECTRIC LINES
4. PRINCIPLES OF ELECTROCHEMISTRY
5. MEASUREMENTS AND MEASURING APPARATUS
6. RESISTORS, RHEOSTATS, CAPACITORS, REACTORS, ELECTROMAGNETS
AND PERMANENT MAGNETS
7. BATTERIES
8. DIRECT-CURRENT MACHINES AND ROTARY ENERGY CONVERTERS
9. ALTERNATING-CURRENT GENERATORS AND MOTORS
10. TRANSFORMERS
11. POWER RECTIFIERS AND INVERTERS
12. SWITCHGEAR AND CONTROL EQUIPMENT
13. POWER STATIONS AND SUBSTATIONS
14. POWER TRANSMISSION AND DISTRIBUTION
15. LIGHTING AND HEATING
10. INDUSTRIAL APPLICATIONS OF MOTORS AND SERVOMECHANISMS
17. TRANSPORTATION
18. ELECTROCHEMICAL AND ELECTROTHERMAL PROCESSES
19. RURAL ELECTRIFICATION DISTRIBUTION SYSTEMS
ELECTRIC COMMUNICATION AND ELECTRONICS
Fourth Edition
BBCT10N
1. MATHEMATICS, UNITS, AND SYMBOLS
2. PROPERTIES OF MATERIALS
3. RESISTORS, INDUCTORS, AND CAPACITORS
4. ELECTRON TUBES
5. ELECTRIC CIRCUITS, LINES, AND FIELDS
6. PASSIVE CIRCUIT ELEMENTS
7. VACUUM TUBE CIRCUIT ELEMENTS
8. FREQUENCY MODULATION
9. PULSE TECHNIQUES
10. TRANSMISSION CIRCUITS
11. ELECTRICAL MEASUREMENTS
12. ACOUSTICS
13. ELECTROMECHANICAI^ACOUSTIC DEVICES
14. OPTICS
15. ELECTRO-OPTICAL DEVICES
16. SOUND REPRODUCTION SYSTEMS
17. TELEPHONY
18. TELEGRAPHY
19. FACSIMILE TRANSMISSION AND RECEPTION
20. TELEVISION
21. ELECTRONIC CONTROL EQUIPMENT
22. AIDS TO NAVIGATION
23. MEDICAL APPLICATIONS OF ELECTRICITY