This Volume is for
REFERENCE USE ONLY
AMERICAN SOCIETY of HEATING
and VENTILATING ENGINEERS
GUIDE, 1935
AN INSTRUMENT OF SERVICE PREPARED FOR THE PROFESSION —
AND CONTAINING REFERENCE DATA ON THE DESIGN AND
SPECIFICATION OF HEATING AND VENTILATING SYSTEMS-
BASED ON THE TRANSACTIONS— THE INVESTIGATIONS OF THE
RESEARCH LABORATORY AND COOPERATING INSTITUTIONS —
AND THE PRACTICE OF THE MEMBERS AND FRIENDS OF THE
SOCIETY
TOGETHER WITH A
MANUFACTURERS' CATALOG DATA SECTION CONTAINING
ESSENTIAL AND RELIABLE INFORMATION CONCERNING MODERN
EQUIPMENT
ALSO
THE ROLL OF MEMBERSHIP OF THE SOCIETY
WITH
COMPLETE INDEXES TO TECHNICAL AND CATALOG DATA
Vol. 13
l5.oo PER COPY
PUBLISHED ANNUALLY BY
AMERICAN SOCIETY of HEATING and VENTILATING
ENGINEERS
ji MADISON AVENUE .'. NEW YORK, N. Y.
COPYRIGHTS 1935
BY
AMERICAN SOCIETY OF HEATING AND VENTILATING ENGINEERS
AND BY IT
DEDICATED
To THE ADVANCEMENT OF
THE PROFESSION
AND
ITS ALLIED INDUSTRIES
TEXT AND ILLUSTRATIONS ARE FULLY PRO-
TECTED BY COPYRIGHT AND NOTHING THAT
APPEARS MAY BE REPRINTED EITHER WHOLLY
OR IN PART WITHOUT SPECIAL PERMISSION.
Printed and Sound ly
THE HORN-SHAFER COMPANY
BALTIMORE :-: MARYLAND
Contents
Page
TITLE PAGE _ i
CONTENTS Hi
PREFACE.- , iv
EDITORIAL ACKNOWLEDGMENT v
CODE OF ETHICS FOR ENGINEERS , vi
CHAPTER 1. Fundamentals of Heating and Air Conditioning 1
CHAPTER 2. Ventilation and Air Conditioning Standards... 33
CHAPTER 3. Industrial Air Conditioning 65
CHAPTER 4. Natural Ventilation . 77
CHAPTER 5. Heat Transmission Coefficients and Tables 91
CHAPTER 6. Air Leakage 119
CHAPTER 7. Heating Load 131
CHAPTER 8. Cooling Load 145
CHAPTER 9. Central Air Conditioning Systems 155
CHAPTER 10. Cooling Methods 165
CHAPTER 11. H modification and Dehumidification 183
CHAPTER 12. Unit Air Conditioners and Conditioning Systems ,.... 197
CHAPTER 13. Unit Heaters, Ventilators, and Coolers 219
CHAPTER 14. Automatic Control—. 239
CHAPTER 15. Air Pollution,. 259
CHAPTER 16. Air Cleaning Devices..... 271
CHAPTER 17. Fans and Motive Power. 281
CHAPTER 18. Sound Control ..'. 299
CHAPTER 19. Air Distribution 317
CHAPTER 20. Air Duct Design 325
CHAPTER 21. Industrial Exhaust Systems 345
CHAPTER 22. Fan Systems of Heating. 359
CHAPTER 23. Mechanical Warm Air Furnace Systems 375
CHAPTER 24. Gravity Warm Air Furnace Systems 389
CHAPTER 25. Boilers - 405
CHAPTER 26. Chimneys and Draft Calculations 423
CHAPTER 27. Fuels and Combustion 443
CHAPTER 28. Automatic Fuel Burning Equipment 457
CHAPTER 29. Fuel Utilization 479
CHAPTER 30. Radiators and Gravity Convectors— 491
CHAPTER 31. Steam Heating Systems 503
CHAPTER 32. Piping for Steam Heating Systems. 527
CHAPTER 33. Hot Water Heating Systems and Piping. 559
CHAPTER 34. Pipe, Fittings, Welding.- 579
CHAPTER 35. Water Supply Piping. 599
CHAPTER 36. Insulation of Piping.__ 623
CHAPTER 37. District Heating.. ^39
CHAPTER 38. Radiant Heating ./657
CHAPTER 39. Electrical Heating ^.~ 667
CHAPTER 40. Test Methods and Instruments... 675
CHAPTER 41. Terminology 685
INDEX TO TECHNICAL DATA 707
CATALOG DATA SECTION - 723
INDEX TO MODERN EQUIPMENT 947
INDEX TO ADVERTISERS™ 959
ROLL OF MEMBERSHIP.™ 1-57
PREFACE TO THE 13th EDITION
THE ambitious plans of the Guide Publication Committee, embodying
several innovations to extend the usefulness of this reference volume,
have been incorporated in this 13th annual edition of THE AMERICAN
SOCIETY OF HEATING AND VENTILATING ENGINEERS GUIDE. The process
of reviewing, revising and reconstructing the Technical Data Section and
then coordinating the complex subject matter of the 41 chapters has
engaged the attention of over 200 members so that THE A.S.H.V.E.
GUIDE 1935 will appeal to an increasing number of readers and give them
comprehensive data that are authoritative and practical.
-Basic and fundamental data have been retained from previous editions
and in those divisions where changes in practice have been observed
modifications have been made in the text to bring the material up-to-date.
The text of THE GUIDE 1935 now comprises two major divisions: the
subject matter of chapters and a supplementary section of the problems
and answers. These problems and their solutions presented as an appen-
dix to each chapter represent the interpretation of the text by a com-
petent engineer whose analysis has been carefully reviewed by the Guide
Publication Committee. It should be understood, however, that for
certain general questions, more than one answer can be made so that the
addition of these questions which represent problems in practice greatly
broadens the scope of THE GUIDE and generally enhances its usefulness.
As developments in the manufacturing field have produced new appa-
ratus and new applications of equipment for automatic heat and air
conditioning to improve comfort, those chapters of THE GUIDE which
discuss such equipment as controls, air washers, unit conditioners, oil
burners, stokers, etc., have been reviewed by representative committees
of engineers from manufacturers' associations so that the latest develop-
ments in their respective fields could be included.
The original conception of THE GUIDE outlined by its founders has
been carefully safeguarded and the aim of the Guide Publication Com-
mittee is to have THE GUIDE 1935 maintain its leadership, and continue
in its role, as the recognized authority in the fields of heating, ventilating
and air conditioning. Thousands of engineers, architects, contractors
and students have come under the influence of THE GUIDE since its first
appearance in 1922 and they have found the data authoritative for their
work in design, specification writing, installation or operation of appa-
ratus and systems.
The Catalog Data of manufacturers is nearly 40 per cent greater in
this current edition indicating that THE GUIDE is also recognized as an
effective advertising medium for promoting the use of modern equipment.
THE GUIDE 1935 contains 150 pages more than the preceding volume
and the Guide Publication Committee release this 13th edition of
10,000 copies, as a major contribution by the Society toward the general
advancement of the engineering profession and its allied industries in the
field of heating, ventilating and air conditioning.
GUIDE PUBLICATION COMMITTEE
W« L. FLEISHER, Chairman
JOHN HOWATT E. N. MCDONNELL
G, L. LARSON W. M. SAWDON
S. R. LEWIS J. H. WALKER
EDITORIAL ACKNOWLEDGMENT
IT is with a profound feeling of pride that the Guide Publication
Committee acknowledges the assistance and cooperation of the many
contributors to the Technical Data Section which appears in THE
GUIDE 1935.
A. J. NESBITT
P. NICHOLLS
PROF. L. S. O'BANNON
G, E. OLSEN
G. H. OSBORNE
J. S. PARKINSON
ALBERT PELLETIER
E. C. RACK
W. C. RANDALL
P. L. REED
W. N. RICH
PROF. T. F. ROCKWELL
C. Z. ROSECRANS
PROF. F. B. ROWLEY
E. B. ROYER
S. S. SANFORD
J. H. SCARR
L. W. SCHAD
W. G. SCHLICHTING
F. E. SEDGWICK
J. G. SHODRON
W. C. SMITH
W. H. SMITH
W. E. STARK
C. W. STEWART
D. J. STEWART
A. G. SUTCLIFFE
D. L. TAZE
L. A. TEASDALE
C. A. THINN
W. W. TIMMIS
C. L. TOONDER
R. N. TRANE
WALTER TUSCH
PROF. G. L. TUVE
W. M. WALLACE, II
F. W. WANDLESS
PERRY WEST
PROF. C. P. YAGLOU
Special mention is due the several Committee members who acted as
division chairmen and who devoted long hours and gave generously of
their knowledge without thought of compensation other than the satis-
faction of contributing to the advancement of the profession. The work
of J. L. Blackshaw as technical assistant in the detailed work of com-
pilation was worthy of special acknowledgment.
T. N. ADLAM
PROF. A. B. ALGREN
H. L. ALT
H. H. ANGUS
W. R. APPELDOORN
O. W. ARMSPACH
F. F. BAHNSON
A. E. BEALS
E. H. BELING
PAULINE BLACKSHAW
J. J. BLOOMFIELD
BERNARD BOCK
C. A. BOOTH
D. S. BOYDEN
J. J. BRAUN
ALBERT BUENGER
C. A. BULKELEY
E. K. CAMPBELL
M. L. CARR
R. E. CHERNE
L. A. CHERRY
P. D. CLOSE
J. F. S. COLLINS, JR.
R. P. COOK
W. E. CRANSTON
A. A. CRIQUI
J. M. DALLAVALLE
M. I. DORFAN
S. H. DOWNS
T. F. DWYER
PROF. E. O. EASTWOOD
Louis ELLIOTT
J0HN EVERETTS, JR.
PROF, M. K. FAHNESTOCK
F. H. FAUST
W. G. FRANK
HUGO FRICKE
W. F. FRIEND
S. L. GOODWIN
DR. F. E. GIESECKE *
W. A. GRANT
DR. LEONARD GREENBURG
HERBERT HERKIMER
J. R. HERTZLER
L. W. HILDRETH
DR. E. VERNON HILL
H. G. HILL
PROF. J. D. HOFFMAN
J. H. HOLTON
F. C. HOUGHTEN
LLOYD HOWELL
PROF. C. M. HUMPHREYS
H. F. HUTZEL
J. W. JAMES
H. B, JOHNS
R. E. JONES
M. G. KERSHAW
D. D. KlMBALL
DR. V. O. KNUDSEN
S. KONZO
PROF. A. P. KRATZ
C. E. LEWIS
E. C. LLOYD
G. W. MARTIN
J. S. M. MATHEWSON
P. F, MCDERMOTT
JOHN McELGiN
WILLIAM McLsisn
H. B. MELLER
R. A. MILLER
DR. C. A. MILLS
D. L. MILLS
F. W. MORSE
O. W. MOTZ
H. C. MURPHY
PROF. D. W. NELSON
s, Chairman
GUIDE PUBLICATION COMMITTEE
CODE of ETHICS for ENGINEERS
ENGINEERING work has become an increasingly important factor
in the progress of civilization and in the welfare of the community.
The engineering profession is held responsible for the planning, construc-
tion and operation of such work and is entitled to the position and
authority which will enable it to discharge this responsibility and to
render effective service to humanity.
That the dignity of their chosen profession may be maintained, it is
the duty of all engineers to conduct themselves according to the principles
of the following Code of Ethics:
I — The engineer will carry on his professional work in a spirit of fairness
to employees and contractors, fidelity to clients and employers, loyalty
to his country and devotion to high ideals of courtesy and personal
honor.
2 — He will refrain from associating himself with or allowing the use of his
name by an enterprise of questionable character.
3 — He will advertise only in a dignified manner, being careful to avoid
misleading statements.
4 — He will regard as confidential any information obtained by him as to
the business affairs and technical methods or processes of a client or
employer.
5 — He will inform a client or employer of any business connections, interests
or affiliations which might influence his judgment or impair the
disinterested quality of his services.
6 — He will refrain from using any improper or questionable methods of
soliciting professional work and will decline to pay or to accept com-
missions for securing such work.
7 — He will accept compensation, financial or otherwise, for a particular
service, from one source only, except with the full knowledge and
consent of all interested parties.
8 — He will not use unfair means to win professional advancement or to
injure the chances of another engineer to secure and hold employment.
9 — He will cooperate in upbuilding the engineering profession by exchang-
ing general information and experience with his fellow engineers and
students of engineering and also by contributing to work of engineering
societies, schools of applied science and the technical press.
10 — He will interest himself in the public welfare in behalf of which he will
be ready to apply his special knowledge, skill and training for the use
and benefit of mankind.
Chapter 1
FUNDAMENTALS OF HEATING AND
AIR CONDITIONING
Dalton's Law, Dry- and Wet-Bulb Temperatures, Properties of
Air, Humidity, Relative Humidity, Specific Humidity, Relation
of Dew Point to Relative Humidity, Adiabatic Saturation of Air,
Total Heat and Heat Content, Enthalpy, Psychrometric Chart,
Properties of Steam, Properties of Water, Rate of Evaporation
AIR conditioning has for its objective the supplying and maintaining,
in a room or other enclosure, of an atmosphere having a composition,
temperature, humidity, and motion which will produce desired effects
upon the occupants of the room or upon materials stored or handled in it.
Dry air is a mechanical mixture of gases composed, in percentage of
volume, as follows1: nitrogen 78.03, oxygen 20.99, argon 0.94, carbon
dioxide 0.03, and small amounts of hydrogen and other gases.
Atmospheric air at sea level is given in percentage by volume as: Ns
77.08, O2 20.75, water vapor 1.2, A 0.93, CO2 0.03 and H2 0.01. The
amount of water vapor varies greatly under different conditions and is
frequently one of the most important constituents since it affects bodily
comfort and greatly affects all kinds of hygroscopic materials.
LAW OF PARTIAL PRESSURES
A mixture of dry gases and water vapor, such as atmospheric air, obeys
Dal ton's Law of Partial Pressures: each gas or vapor in a mixture, at a
given temperature, contributes to the observed pressure the same amount
that it would have exerted by itself at the same temperature had no other
gas or vapor been present. If p — the observed pressure of the mixture
and p^ p2, ps, etc. = the pressure of the gases or vapors corresponding to
the observed temperature, then
P = pi + pz + p3, etc. (1)
DRY- AND WET-BULB TEMPERATURES
Air is said to be saturated at a given temperature when the water vapor
mixed with the air is in the dry saturated condition or, what is the equiv-
alent, when the space occupied by the mixture holds the maximum pos-
sible weight of water vapor at that temperature. If the water vapor
mixed with the dry air is superheated, i.e., if its temperature is above the
temperature of saturation for the actual water vapor partial pressure, the
air is not saturated.
^International Critical Tobies.
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
The starting point of most applications of thermodynamic principles to
air-conditioning problems is the experimental determination of the dry-
bulb and wet-bulb temperatures, and sometimes the barometric pressure.
The dry-bulb temperature of the air is the temperature indicated by any
type of thermometer not affected by the water vapor content or relative
humidity of the air. The 'wet-bulb temperature is determined by a thermo-
meter with its bulb encased in a fine mesh fabric bag moistened with clean
water and whirled through the arir until the thermometer assumes a
steady temperature. This steady temperature is the result of a dynamic
equilibrium between the rate at which heat is transferred from the air to
the water on the bulb and the rate at which this heat is utilized in evapor-
ating moisture from the bulb. The rate at which heat is transferred from
the air to the water is substantially proportional to the wet-bulb depres-
sion (t — £l), while the rate of heat utilization in evaporation is propor-
tional to the difference between the saturation pressure of the water at
the wet-bulb temperature and the actual partial pressure of the water
vapor in the air (e] — e). Carriers equation for this dynamic equilibrium
is
t - t1 2800 - 1.3*'
In the form commonly used,
(2a)
^ J
2800 - L3*1
where
e = actual partial pressure of water vapor in the air, inches of mercury.
e1 - saturation pressure at wet-bulb temperature, inches of mercury.
B ~ barometric pressure, inches of mercury.
t = dry-bulb temperature, degrees Fahrenheit.
/« ss wet-bulb temperature, degrees Fahrenheit.
Formula 2b may be used to determine the actual partial pressure of the
water vapor in a dry air-water vapor mixture. Then, from Dalton's Law
of Partial Pressures, Equation 1, it follows that the partial pressure of the
dry air is (B — e).
If a mixture of dry air and water vapor, initially unsaturated, be cooled
at constant pressure, the temperature at which condensation of the water
vapor begins is called the dew-point temperature. Clearly the dew-point
is the saturation temperature corresponding to the actual partial pressure,
e, of the water vapor in the mixture.
PROPERTIES OF AIR
Density is variously defined as the mass per unit of volume, the weight
per unit of volume, or the ratio of the mass, or weight, of a given volume
of a substance to the mass, or weight, of an equal volume of some other
substance such as water or air under standard conditions of temperature
and pressure. The term specific gravity is more commonly used to express
the latter relation but, when the gram is taken as the unit of mass and the
cubic centimeter as the unit of volume, density and specific gravity have
CHAPTER I-^-FUNDAMENTALS OF HEATING AND AIR CONDITIONING
%
the same meaning. The term specific density is sometimes used to dis-
tinguish the weight in pounds per cubic foot; and as here used, density is
the weight in pounds of one cubic foot of a substance.
The density of air decreases with increase in temperature when under
constant pressure. The density of dry air at 70 F and under standard
atmospheric pressure (29.92 in. of Hg) is approximately 0.075 Ib (see
Table 1), while that of a mixture of air and saturated water vapor at the
same temperature and barometric pressure is only about 0.0743 Ib. In
the mixture the density of the dry air is 0.0731 and that of the vapor is
0.001 15 Ib (see Table 2).
In order to make comparisons of air volumes or velocities it is necessary
to reduce the observations to a common pressure and temperature basis.
The basic pressure is usually taken as 29.92 in. of Hg, but no basic tem-
perature is universally recognized. Common temperatures for this
purpose are 32 F, 60 F, 68 F, and 70 F. Since 70 F is the most commonly
specified temperature to which rooms for human occupancy must be
heated, it is usually understood, when no other temperature is specified,
that 70 F is the basic temperature for measuring the volume or the
velocity of air in heating and ventilating work.
The specific volume of air is the volume in cubic feet occupied by one
pound of the air. Under constant pressure the specific volume varies
inversely as the density and directly as the absolute temperature.
The specific heat of air is the number of Btu required to raise the
temperature of 1 Ib of air 1 F. The specific heat at constant pressure,
Cp, and that at constant volume, Cv, are different. The specific heat
at constant pressure is commonly used and it varies, under a pressure
of one atmosphere, from a minimum at about 32 F from which it increases
with either increase or decrease of temperature. The value 0.24 is suf-
ficiently accurate for use at ordinary temperatures, but the values range1
from 0.2399 at 32 F to 0.2404 at 212 F, 0.2413 at 392 F, 0.243 at - 108 F,
and 0.252 at -301 F.
The mean specific heat of water vapor at constant pressure is taken as
0.45 for all general engineering computations.
Table 3 is intended to aid in determining the density of moist air,
taking into account its temperature, pressure, and moisture content.
Example 1. To show the use of Table 3: Given air at 83 F dry-bulb and 68 F wet-
bulb (or a depression of 15 deg) with a barometric pressure of 29.40 in. of mercury.
What will be the weight of this air in pounds per cubic foot?
Solution. From Table 3 the weight of saturated air at 80 F and 29.00 in. barometer is
found to be 0.07034 Ib per cubic foot. There is a decrease of 0.00015 Ib per degree dry-
bulb temperature above 80 F. There is an increase of 0.00025 Ib for each 0.1 in. above
29.00 in. From the last column of Table 3 it is found that there is an increase of approxi-
mately 0.000035 Ib per degree wet-bulb depression when the dry-bulb is 83 F. Tabu-
lating the items:
0.07034 = weight of saturated air at 80 F and 29.00 bar.
- 0.00045 = decrement for 3 deg dry-bulb, 3 X 0.00015.
+ 0.00100 = increment for 0.4 in. bar., 4 X 0.00025.
-f 0.00053 = increment for 15 deg wet-bulb depression, 15 X 0.000035.
0.07142 — weight in pounds per cubic foot of air at 83 F dry-bulb, 68 F wet-bulb,
29.40 in. bar.
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 1. PROPERTIES OF DRY Ama
Barometric Pressure 29.921 In.
TEMPERATURE
DBS P
WEIGHT PER Cu FT
POUNDS
PER CENT OP VOLUME
AT70F
BTXT ABSORBED BY
ONE Cu FT DRY AIR
PER DEG F
Cu FT DRY Am
WARMED ONE DEGREE
PER BTU
0
0.08636
0.8680
0.02080
48.08
10
0.08453
0.8867
0.02039
49.05
20
0.08276
0.9057
0.01998
50.05
30
0.08107
0.9246
0.01957
51.10
40
0.07945
0.9434
0.01919
52.11
50
0.07788
0.9624
0.01881
53.17
60
0.07640
0.9811
0.01846
54.18
70
0.07495
1.0000
0.01812
55.19
80
0.07356
1.0190
0.01779
56.21
90
0.07222
1.0380
0.01747
57.25
100
0.07093
1.0570
0.01716
58.28
110
0.06968
1.0756
0.01687
59.28
120
0.06848
1.0945
0.01659
60.28
130
0.06732
1.1133
0.01631
61.32
140
0.06620
1.1320
0.01605
62.31
150
0.06510
1.1512
0.01578
63.37
160
0.06406
1.1700
0.01554
64.35
180
0.06205
1.2080
0.01506
66.40
200
0.06018
1.2455
0.01462
68.41
220
0.05840
1.2833
0.01419
70.48
240
0.05673
1.3212
0.01380
72.46
260
0.05516
1.3590
0.01343
74.46
280
0.05367
1.3967
0.01308
76.46
300
0.05225
1.4345
0.01274
78.50
350
0.04903
1.5288
0.01197
83.55
400
0.04618
1.6230
0.01130
88.50
450
0.04368
1.7177
0.01070
93.46
500
0.04138
1.8113
0.01018
98.24
550
0.03932
1.9060
0.00967
103.42
600
0.03746
2.0010
0.00923
108.35
700
0.03423
2.1900
0.00847
11$. 07
800
0.03151
2.3785
0.00782
127.88
900
0.02920
2.5670
0.00728
137.37
1000
0.02720
2.7560
0.00680
147.07
•From Fan Engineering*
CHAPTER 1 — FUNDAMENTALS OF HEATING AND AIR CONDITIONING
It is usual to assume that dry air, moist air, and the water vapor in the
air follow the laws of perfect gases. This assumption while not absolutely
true, especially with saturated vapor at temperatures much above 140 F,
TABLE 2. PROPERTIES OF SATURATED Araa
Weights of Air, Vapor of Water, and Saturated Mixture of Air and Vapor at 29.921 Inches of Mercury
TEMP.
DEG.F
WEIGHT IN A CTTBIC FOOT OF MITTUBE
BTU ABSORBED BT
ONE CUBIC FOOT
SAT. Am PER
DEGF
CUBIC FEET SAT.
Am WABMED ONE
DEGREE PER
BTU
SPECIFIC
HEAT BTU
PER POUND
OlMlXTUKI
WEIGHT OP
DRY Am
POUNDS
WEIGHT OP
VAPOE
POUNDS
TOTAL WEIGHT OP
THE MDCTURE
POUNDS
0
0.08625
0.000068
0.08632
0.02083
48.02
0.2413
10
0.08433
0.000110
0.08444
0.02039
49.05
0.2415
20
0.08246
0.000176
0.08264
0.01998
50.07
0.2418
30
0.08062
0.000277
0.08090
0.01958
51.07
0.2420
40
0.07878
0.000409
0.07919
0.01921
52.06
0.2426
50
0.07694
0.000587
0.07753
0.01885
53.05
0.2431
60
0.07506
0.000828
0.07589
0.01851
54.02
0.2439
70
0.07310
0.001151
0.07425
0.01819
54.97
0.2450
80
0.07103
0.001578
0.07261
0.01790
55.87
0.2465
90
0.06879
0.002134
0.07092
0.01762
56.76
0.2485
100
0.06635
0.002850
0.06920
0.01736
57.59
0.2509
110
0.06364
0.003762
0.06740
0.01714
58.35
0.2543
120
0.06060
0.004914
0.06551
0.01695
59.00
0.2587
130
0.05715
0.006351
0.06350
0.01679
59.56
0.2644
140
0.05319
0.008120
0.06131
0.01668
59.96
0.2721
150
0.04864
0.010295
0.05894
0.01662
60.17
0.2820
160
0.04340
0.012936
0.05634
0.01662
60.17
0,2950
170
0.03734
0.016108
0.05345
0.01668
59.96
0.3121
ISO
0.03035
0.019896
0.05025
0.01684
59.38
0.3351
190
0.02228
0.024400
0.04668
0.01710
58.49
0.3663
200
0.01300
0.029715
0.04272
0.01749
57.18
0.4094
210
0.00230
0.035938
0.03824
0.01802
55.50
0.4712
212
0.00000
0.037307
0.03731
0.01815
55.10
0.4865
aFroip. Fan Engineering.
is sufficiently accurate for practical purposes and it greatly simplifies
computations.
Boyle's Law refers to the relation between the pressure and volume of a
gas, and may be stated as follows : With temperature constant, the volume of
a given weight of gas varies inversely as its absolute pressure. Hence, if
PI and P2 represent the initial and final absolute pressures, and V\ and
F2 represent corresponding volumes of the same mass, say one pound of
V P
gas, then •=? = --, or PI FI = P2 F2, but since PI FI for any given case is
a definite constant quantity, It follows that the product of the absolute
5
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
5 «
Ii
H
c^
s
2
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CHAPTER 1 — FUNDAMENTALS OF HEATING AND AIR CONDITIONING
pressure and volume of a gas is a constant, or PV = C, when T is kept
constant. Any change in the pressure and volume of a gas at constant
temperature is called an isothermal change.
Charles1 Law refers to the relation among pressure, volume, and tem-
perature of a gas and may be stated as follows: The volume of a given
weight of gas varies directly as the absolute temperature at constant pressure,
and the pressure varies directly as the absolute temperature at constant
volume. Hence, when heat is added at constant volume, Fc, the resulting
~P T
equation is ~ = •—, or, for the same temperature range at constant pres-
-t i l\
sure, PC, the relation is ~ = •—.
In general, for any weight of gas, W, since volume is proportional to
weight, the relation among P, V, and T is
PV = WRT (3)
where
P — the absolute pressure of the gas, pounds per square foot.
V = the volume of the weight W, cubic feet.
W — the weight of the gas, pounds.
R = a constant depending on the nature of the gas. The average value of R for air
is 53.34.
T = the absolute temperature, degrees Fahrenheit.
This is the characteristic equation for a perfect gas, and while no gases
are perfect in this sense, they conform so nearly that Equation 3 will
apply to most engineering computations.
HUMIDITY
Humidity is the water vapor mixed with dry air in the atmosphere.
Absolute humidity has a multiplicity of meanings, but usually the term
refers to the weight of water vapor per unit volume of space occupied,
expressed in grains or pounds per cubic foot. With this meaning, absolute
humidity is nothing but the actual density of the water vapor in the
mixture and might better be so called. A study of Keenan's Steam
Tables2 indicates that water vapor, either saturated or super-heated, at
partial pressures lower than 4 in. of mercury may be treated as a gas with
a gas constant R of 1.21 in the characteristic equation of the gas pV =
wR (t + 460). Within such limits, the density (8) of water vapor is
(pounds per cubic foot) (4a)
1.21 (t + 460)
5785 e (grains per cubic foot) (4b)
t + 460
where
e = actual partial pressure of vapor, inches of mercury*
t = dry-bulb temperature, degrees Fahrenheit.
•Published by American Society of Mechanical Engineers, see abstract in Table 7.
7
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Specific Humidity
It simplifies many problems which deal with mixtures of dry air and
water vapor to express the weight or the mass of the vapor in terms of the
weight or the mass of dry air. If the weight of the water vapor in a
mixture be divided by the weight of the dry air, and the weight of dry air
be made unity, we have an expression of the weight of water vapor carried
by a unit weight of dry air. This relation has no generally accepted name.
It has been variously called: mixing ratio, proportionate humidity, mass
or density ratio, absolute humidity, and specific humidity. Of all these
terms specific humidity is the most suggestive of the meaning which it is
desired to express and it has found considerable use in this sense even
though it is defined in International Critical Tables as the ratio of the
mass of vapor to the total mass. It will be understood here that specific
humidity refers to the weight of water vapor in pounds carried by one
pound of dry air.
The gas constant for dry air, when the partial pressure of the air is
expressed in inches of Hg, is 0.753; so that the specific humidity, if
represented by IF, is
w/ e - B~e
W =
1.21 (/ H- 460) ' 0.753 (/ + 460)
= 0.622 (~-\ (pounds) (5a)
= 4354 ( jl~\ (grains) (5b)
where
e = actual partial pressure of vapor, inches of mercury.
B = total pressure of mixture (barometric pressure), inches of mercury.
Relative Humidity
Relative humidity ($) is either the ratio of the actual partial pressure,
e, of the water vapor in the air to the saturation pressure, et, at the dry-
bulb temperature, or the ratio of the actual density, 8, of the vapor to
the density of saturated vapor, 8t, at the dry-bulb temperature. That is:
*-i = i (6)
The relative humidity of a given mixture at af given temperature is not
the same as the specific humidity, Wt of the mixture divided by the
specific humidity, Wt, of saturated vapor at the same temperature, for
from Equations 5a and 6
0.622 - - (7)
< _ . -
Wt \P — 3> et/ \ B-et ) B —
The specific humidity of an unsaturated air-vapor mixture cannot,
therefore, be accurately found by multiplying the specific humidity of
saturated vapor by its relative humidity; although the error is usually
small especially when the, relative humidity is high.
With a relative humidity of 100 per cent, the dry-bulb, wet-bulb, and
8
CHAPTER 1 — FUNDAMENTALS OF HEATING AND AIR CONDITIONING
dew-point temperatures are equal. With a relative humidity less than
100 per cent, the dry-bulb exceeds the wet-bulb, and the wet-bulb exceeds
the dew-point temperature.
RELATION OF DEW POINT TO RELATIVE, HUMIDITY
A peculiar relationship exists between the dew point and the relative
humidity and this is found most useful in air conditioning work. This
relationship is, that for a fixed relative humidity there is substantially a
constant difference between the dew point and the dry-bulb temperature
over a considerable temperature range. Table 4, giving the dry-bulb and
dew-point temperatures and the dew-point differentials for 50 per cent
relative humidity, illustrates this relationship clearly.
TABLE 4.
DRY-BULB AND DEW-POINT TEMPERATURES FOR
50 PER CENT RELATIVE HUMIDITY
Dry-bulb temperature
65.0
70.0
75.0
80.0
85.0
90.0
Dew-point temperature
45.8
50.5
55.25
59.75
64.25
68.75
Difference between dew-point and dry-
bulb temperature
19.2
19.5
19.75
20.25
20.75
21.25
It will be seen from an inspection of this table that the difference
between the dew-point temperature and the room temperature is approxi-
mately 20 deg throughout this range of dry-bulb temperatures or, to
be more exact, the differential increases only 10 per cent for a range of
practically 25 deg.
This principle holds true for other humidities and is due to the fact
that the pressure of the water vapor practically doubles for .every 20 deg
through this range*
The approximate relative humidity for any difference between dew-
point and dry-bulb temperature may be expressed in per cent as:
100
(8)
where
dew-point temperature.
This principle is very useful in determining the available cooling effect
obtainable with saturated air when a desired relative humidity is to }>e
maintained in a room, even though there may be a wide variation in room
temperature. This problem is one which applies to certain industrial con-
ditions, such as those in cotton mills and tobacco factories, where re-
latively high humidities are carried and where one of the principal prob-
lems is to remove the heat generated by the machinery. It also permits
the use of a differential thermostat, responsive to both the room tempera-
ture and the dew-point temperature, to control the relative humidity
in the room.
Table 5 gives, for different temperatures, the density of saturated vapor,
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
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CHAPTER 1 — FUNDAMENTALS OF HEATING AND AIR CONDITIONING
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
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CHAPTER 1 — FUNDAMENTALS OF HEATING AND AIR CONDITIONING
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
St, the weight of saturated vapor mixed with 1 Ib of dry air, Wt, (at a
relative humidity of 100 per cent and a barometric pressure, B, of 29.92 in.
of mercury) , the specific volume of dry air, and the volume of an air- vapor
mixture containing 1 Ib of dry air (at a relative humidity of 100 per cent
and a pressure of 29.92 in. of mercury). The preceding equations or the
data from Table 5 may be conveniently used in solving the following
typical problems : (See Table 6 for temperatures below OF.)
Example 2. Humidifying and Heating. Air is to be maintained at 70 F with a relative
humidity of 40 per cent (3? — 0.4) when the outside air is at 0 F and 70 per cent
relative humidity (<£ == 0.7) and a barometric pressure, B, of 29.92 in. of mercury. Find
the weight of water vapor added to each pound of dry air and the dew-point temperature
of the humidified air.
Solution. From Equation 5a and Table 5,
0.622 X_Q° = °-000547 lb Per P°und of dT air-
°*°0618 lb per P°Und °f dry air'
The water vapor added per pound of dry air must be (Wz - Wi) or 0.005633 lb. By
inspection of Table 5, Wt = 0.00618 at 44.5 F, so this is the dew-point temperature of
the humidified air.
An approximation of the same result from Table 5 is
Wi = 0.7 X 0.000781 » 0.000547 lb per pound of dry air.
W2 = 0.4 X 0.01578 = 0.006312 lb per pound of dry air.
The water vapor added per pound of dry air is approximately 0.005765 lb and the
dew-point temperature is approximately 45 F. The degree of approximation is evident.
Example #. Dehumidifying and Cooling. Air with a dry-bulb temperature of 84 F,
a wet-bulb of 70 F, or a relative humidity of 50 per cent (<3> = 0.5), and a barometric
pressure, 5, of 29.92 in. of mercury is to be cooled to 54 F. Find the dew-point tem-
perature of the entering air and the weight of vapor condensed per pound of dry air.
Solution. From Equation 5a and Table 5,
Wi = 0.622 (29 ^-^Q1 587) = °-01245 lb Per P°und of ^ ain
w, = 0.622 (2992^042) " °-00887 lb Per p°und of dry air-
Since Wi = Wt when / = 63.3 F, this is the dew-point temperature of the entering air.
The weight of vapor condensed is (W\ — Wz) or 0.00358 lb per pound of dry air.
An approximate result is
Wi = 0.5 X 0.02547 = 0.01274 lb per pound of dry air.
Wi = 1 X 0.00887 = 0.00887 lb per pound of dry air, since the exit air is saturated.
Since Wi = Wt at t - 64 F, this is the dew-point temperature of the entering air.
The^weight of vapor condensed is 0.00387 lb per pound of dry air. The degree of approxi-
mation is again evident.
ADIABATIC SATURATION OF AIR
The process of adiabatic saturation of air is of considerable importance
in air-conditioning. Suppose that 1 lb of dry air, initially unsaturated but
carrying W lb of water vapor with a dry-bulb temperature, t, and a wet-
14
CHAPTER 1 — FUNDAMENTALS OF HEATING AND AIR CONDITIONING
bulb temperature, f, be made to pass through a tunnel containing an
exposed water surface. Further assume the tunnel to be completely in-
sulated, thermally, so that the only heat transfer possible is that between
the air and water. As the air passes over the water surface, it will gradu-
ally pick up water vapor and will approach saturation at the initial wet-
bulb temperature of the air, if the water be supplied at this wet-bulb tem-
perature. During the process of adiabatic saturation, then, the dry-bulb
temperature of the air drops to the wet-bulb temperature as a limit, the
wet-bulb temperature remains substantially constant, and the weight of
water vapor associated with each pound of dry air increases to Wv, as a
limit, where Wv is the weight of saturated vapor per pound of dry air for
saturation at the wet-bulb temperature.
Example 4- If air with a dry-bulb of 85 F and a wet-bulb of 70 F be saturated adia-
batically by spraying with recirculated water, what will be the final temperature and the
vapor content of the air?
Solution. The final temperature will be equal to the initial wet-bulb temperature or
70 F, and since the air is saturated at this temperature, from Table 5, W = 0.01578 Ib
per pound of dry air.
In the adiabatic saturation process, since the heat given up by the dry
air and associated vapor in cooling to the wet-bulb temperature is utilized
in evaporation of water at the wet-bulb temperature, W. H. Carrier has
pointed out3 that the equation for the process of adiabatic saturation, and
hence for a process of constant wet-bulb temperature, is:
fc'fg (Wti - W) - cPa (t - *') + c^W (t ~ *') (9a)
and using cPa = 0.24 and cPs = 0.45
#fc (Wv - W) = (0.24 -f 0.4517) (t - f) (9b)
where
h*fs — latent heat of vaporization at t1, Btu per pound.
(Wt* — W) = increase in vapor associated with 1 Ib of dry air when it is saturated
adiabatically from an initial dry-bulb temperature, /, and an initial vapor content, W,
pounds.
Knowing any two of the three primary variables, /, t', or W, the third
may be found from this equation for any process of adiabatic saturation.
TOTAL HEAT AND HEAT CONTENT
The total heat of a mixture of dry air and water vapor was originally
defined by W. H. Carrier as
S = <;Pa (t - 0) -f W [fc'fg + cPs (t - *')] (10)
where
2 = total heat of the mixture, Btu per pound of dry air.
Cp^ = mean specific heat at constant pressure of dry air.
Cpg =s mean specific heat at constant pressure of water vapor.
t = dry-bulb temperature, degrees Fahrenheit.
# = wet-bulb temperature, degrees Fahrenheit.
*A.SM.E. Transactions, Vol. 33, 1911, p. 1005.
15
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 6. PROPERTIES OF SATURATED WATER VAPOR AT LOW/TEMPERATURES**
Barometer, 29.92 Inches of. Mercury
WEIGHT OP
WEIGHT OP
TEMPERA-
VAPOR
PRESSURE
SATURATED
VAPOR
BTU PER LB
OF VAPOR
TEMPERA-
VAPOR
PBESSURB
SATURATED
VAPOR
BTU PER LB
OF VAPOR
TUBE
IN
PER LB
(32 F
TURE
IN.
PBRLfi
(32 F
F
Hex 10-6
DRY AIR
DATUM)
F
HoX 10-6
DRY AIR
DATUM)
X1QJ
X 10-6
-130
0.276
0.005738
1000.7
-85
15.87
0.3299
1021.0
-129
.306
.006362
1001.2
-84
17.20
- .3576
•1021.4
-128
.338
.007027
1001.6
-83
18.58
,.3863
1021.9
-127
.373
.007755
1002.1
-82
20.10
.4179
1022.3
-126
.411
.008545
1002.5
-81
21.72
.4516
1022.8
-125
.455
.009459
1003.0
-80-
23.47
.4879
1023.2
-124
.499
.01037
1003.4
-79
25.34
.5268
1023.7
-123
.542
.01127
1003.9
-78
27.29
.5674
1024.1
-122
-.604
.01256
1004.3
-77
29.52
- .6137
1024.6
-121
.669
.01391
1004.8
-76
31.81
.6613
1025.0
-120
.735
.01528
1005.2
-75
34.37
.7146
1025.5
-119
.805
.01674
1005.7
-74
37.01
.7694
1025.9
-118
.892
.01854
1006.1
-73
39.96
.8308
1026.4
-117
.989
.02056
1006.6
-72
43.04
.8948
1026.8
-116
1.098
.02283
1007.0
-71
46.33
.9632
1027.3
-115
'1.208
.02511
1007.5
-70
49.87
1.037
1027.7
-114
1.317
.02738
1007.9
-69
53.59
1.114
1028.2
-113
1.444
.03002
1008.4
-68
57.65
1.199
1028.6
-112
1.575
.03274
1008.8
-67
61.81
1.285
1029.1
-111
1.728
.03593
1009.3
-66
66.41
1.381
1029.5
-110
1.889
.03927
1009.7
-65
71.17
1.480
1030.0
-109
2.087
.04339
1010.2
-64
76.64
1.593
1030.4
-108
2.292
.04765
1010.6
-63
82.28
1.711
1030.9
-107
2.511
.05220
1011.1
-62
88.19
•1.833
1031.3
-106
2.742
.05701
1011.5
-61
94.62
1.967
1031.8
-105
2.983
.06202
1012.0
-60
101.4
2.108
1032.2 *
-104
3.258
.06773
1012.4
-59
108.8
2.262
1032.7
-103
3.543
.07366
1012.9
-58
116.3
2.418
1033.1
-102
'3.872
.08050
1013.3
-57
124.8
2.595
1033.6
-101
4.213
.08759
1013.8
-56
133.4
2.773
1034.0
-100
4.607
.09578
1014.2
-55
143.0
2.973
1034.5
-99
5.018
.1043
1014.7
-54
153.0
3.181
1034.9
-98
5.455
.1134
1015.1
-53
163.5
3.399
1035.4
-97
5.946
.1236
1015.6
-52
174.9
3.636
1035.8
-96
6.470
.1345
1016.0
-51
187.0
3.888
1036.3
-95
7.047
.1465
1016.5
-50
199.9
4.156
1036.7
-94
7.638
.1588
1016.9
-49
213.0
4.428
1037.2
-93
8.316
.1729
1017.4
-48
227.9
4.738
1037.6
-92
9.017
.1875
1017.8
-47
243.1
5.054
1038.1
' -91
9.806
.2039
1018.3
-46
259.5
5.395
1038.5
-90
10.64
.2212
1018.7
-45
276.7
5.753
1039.0
-89
11.53
.2397
1019.2
-44
295.0
6.133
1039.4
-88
12.51
.2601
1019.6
-43
314.7
6.543
1039.9
-87
13.53
.2813
1020.1
-42
335.3
6.971
1040.3
-86
14.69
.3054
1020.5
-41
357.6
7.435
1040.8
" "Vapor pressures converted from International Critical Tables.
16
CHAPTER 1— FUNDAMENTALS OF HEATING AND AIR CONDITIONING
TABLE 6. PROPERTIES OF SATURATED WATER VAPOR AT Low TEMPERATURES** (Con'd.)
Barometer, 29.92 Inches of Mercury
WEIGHT OF
WEIGHT OF
TEMPEBA-
TTJRE
F
VAPOB
PEESSTJHE
IN.
Ho X 10-5
SATURATED
VAPOR
PERL-B
DRT Am
Bru PEE LB
OP VAPOR
(32 F
DATUM)
TEMPERA-
TURE
F
VAPOR
PRESSURE
IN.
EG X 10-5
SATURATED
VAPOR
FERliB
DRY AIR
BTU PER LB
OF VAPOR
(32 F
DATUM)
X 10-5
X 10-s
-40
380.3
7.907
1041.2
-20
1262.0
26.25
1050.2
-39
405.5
8.431
1041.7
-19
1337.
27.81
1050.7
-38
431.2
8.965
1042.1
-18
1416.
29.45
1051.1
-37
459.2
9.548
1042.6
-17
1496.
31.12
1051.6
-36
488.4
10.16
1043.0
-16
1584.
32.95
1052.0
-35
519.5
10.80
1043.5
-15
1675.
34.84
1052.5
-34
552.4
11.49
1043.9
-14
1772.
36.86
1052.9
-33
586.5
12.20
1044.4
-13
1874.
38.98
1053.4
-32
623.7
12.97
1044.8
-12
1980.
41.19 '
1053.8
-31
661.8
13.76
1045.3
-11
2093.
43.54
1054.3
-30
701.0
14.58
1045.7
-10
2210.
45.98
1054.7
-29
742.2
15.43
1046.2
-9
2335.
48.58
1055.2
-28
791.2
16,45
1046.6
-8
2463.
51.25
1055.6
-27
841.0
17.49
1047.1
-7
2502.
52.06
1056.1
-26
892.1
18.55
1047.5
-6
2745.
57.12
1056.5
-25
946.4
19.68
1048.0
-5
2898.
60.30
1057.0
-24
1003.
20.86
1048.4
-4
3055.
63.57
1057.4
-23
1064.
22.13
1048.9
-3
3222.
67.05
1057.9
-22
1126.
23.42
1049.3
-2
3397.
70.69
1058.3
-21
1192.
24.79
1049.8
-1
3580.
74.50
1058.8
0
3773.
78.52
1059.2
a Vapor pressures converted from International Critical Tables,
W = weight of water vapor mixed with each pound of dry air, pounds,
ft'fg = latent heat of vaporization at tl, Btu per pound.
Since this definition holds for any mixture of dry air and water vapor,
the total heat of a mixture with a relative humidity of 100 per cent and at
a temperature equal to the wet-bulb temperature (/!) is
- 0)
(11)
By equating Equation 10 to Equation 11, the equation for the adiabatic
saturation process, Equation 9a, follows. This demonstrates that the
adiabatic saturation process at constant wet-bulb temperature is also a
process of constant total heat. In short, the total heat of a mixture of dry
air and water vapor is the same for any two states of the mixture at the
same wet-bulb temperature. This fact furnishes a convenient means of
finding the total heat of an air-vapor mixture in any state.
Example 5. Find the total heat of an air-vapor mixture having a dry-bulb tempera-
ture of 85 F and a wet-bulb temperature of 70 F.
Solution. From Table 5, for saturation at the wet-bulb temperature Wv = 0.01578,
and from Equation 11,
Sr = Cpa (70 - 0) + 0.01578 Wtg = 16.9 + 16.61 = 33.51
17
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
By 'considering the temperatures in Table 5 to be wet-bulb readings, the
total heat of any air- vapor mixture may be obtained from the last column
in the table.
Enthalpy
This total heat of an air-vapor mixture is not exactly equal to the true
heat content or enthalpy of the mixture since the heat content of the
liquid is not included in Equation 10. • With the meaning of heat content
in agreement with present practise in other branches of thermodynamics,
the true heat content of a mixture of dry air and water vapor (with 0 F
as the datum for dry air, and the saturated liquid at 32 F as the datum
for the water vapor) is
h = cPa (t - 0) 4- W hs = 0.24 (* - 0) + W hs (12)
where
h = the heat content of the mixture, Btu per pound of dry air.
t = the dry-bulb temperature, degrees Fahrenheit.
W = the weight of vapor per pound of dry air, pounds.
7fs = the heat content of the vapor in the mixture, Btu per pound.
The heat content of the water vapor in the mixture may be found in
steam charts or tables when the dry-bulb temperature and the partial
pressure of the vapor are known. Or, since the heat content of steam at
low partial pressures, whether super-heated or saturated, depends only
upon temperature, the following empirical equation, derived from
Keenan's Steam Tables, may be used:
hs = 1059.2 + 0.45 t (13)
Substituting this value of hs in Equation 12, the heat content of the
mixture is
h = 0.24 (t - 0) + W (1059.2 + 0.45 t} (14)
An energy equation can be written that applies, in general, to various
air-conditioning processes, and this equation can be used to determine the
quantity of heat transferred during such processes. In the most general
form, this equation may be explained with the aid of Fig. 1 as follows:
The rectangle may represent any apparatus, e.g., a drier, humidifier, dehumidifier,
cooling tower, or the like, by proper choice of the direction of the arrows.
In general, a mixture of air and water vapor, such as atmospheric air, enters the
apparatus at 1 and leaves at 3. Water is supplied at some temperature, fe. For the flow
of 1 Ib of dry air (with accompanying vapor) through the apparatus, provided there is no
appreciable change in the elevation or velocity of the fluids and no mechanical energy
delivered to or by the apparatus,
or
Eh - Re = ^ - A! - (W* - Wi) Jh (15)
where
Eh - the quantity of heat supplied per pound of dry air, Btu.
j£c = the quantity of heat lost externally by heat transfer from the ^apparatus,
Btu per pound of dry air.
18
CHAPTER 1 — FUNDAMENTALS OF HEATING AND AIR CONDITIONING
Wi = the weight of water vapor entering, per pound of dry air.
Ws = the weight of water vapor leaving, per pound of dry air.
fh — the heat content of the water supplied at t», Btu per pound.
hz — hi — the increase 'in the heat content of the air- water vapor mixture in passing
through the apparatus, Btu per pound of dry air
- 0.24 (fe - fr) -f Wz (1059.2 + 0.45 fc) - Wl (1059.2 -f 0.45*0
The net quantity of heat added to or removed from air-water vapor
mixtures in air conditioning work is frequently approximated by taking
the differences in total heat at exit and entrance.
For example, in Fig. 1, an approximate result is
Eh - Re = S3 - Si (16)
where
23 = the total heat of the air-vapor mixture at exit, Btu per pound of dry air.
Si — the total heat of the air- vapor mixture at entrance, Btu per pound of dry air.
From the definitions of total heat and heat content, it may be demon-
strated that Equation 16 is exactly equivalent to Equation 15, when, and
only when, ^3 = t\ — fe; i.e., when the initial and final wet-bulb tempera-
tures and the temperature of the water supplied are equal. The one pro-
cess that meets these conditions is adiabatic saturation, and either
equation will give a result of zero; for other conditions, Equation 16 is
approximate 'but satisfactory for many calculations.
. The following problems illustrate the application of these principles:
Example 6. Heating (data from Example 2). Assuming the water to be supplied at
50 F, the net quantity of heat supplied is, from Equation 15,
JSJk - jRe = 0.24 (70 - 0) + 0.000547 X 0.45 (70 - 0) -f 0.005633
or
1059.2 -f 0.45 X 70 - (50 - 32) = 22.87 Btu per pound of dry air.
Example 7. Cooling (data from Example 3). If the condensate is removed at 54 F
the quantity of heat removed is found from Equation 15, by proper regard to the arrow
direction in Fig. 1,
Eh + J?c = 0.24 (84 - 54) -f 0.00887 X 0.45 (84 - 54) + 0.00358
or
1059.2 + 0.45 X 84 - (54 - 32) = 11. 17 Btu per pound of dry air.
Using Table 5, the initial total heat of the air-vapor mixture, since the wet-bulb
temperature is 70 F, is 33.51 Btu per pound of dry air.
The final total heat is, from Table 5, since the exit air is saturated, 22.45 Btu per
pound. Hence, using Equation 16, the quantity of heat removed is, approximately,
(33.51 — 22.45) or 11.06 Btu per pound of dry air. The degree of approximation to the
correct result is evident in this example.
PSYCHROMETRIC CHART4
The Bulkeley Psychrometric Chart5, as revised will be found as an
insert between pages 18 and 19. It shows graphically the relationships
expressed in Equations 9a and 9b. It also gives the grains of moisture per
*See A Review of Psychrometric Charts, C. O. Mackey (Heating and Ventilating* June, July, 1931V
•The- Bulkeley Psychrometric Chart was presented to the Society in 1926. , (See A.S.H.V.E. Tsu
ACTIONS, Vol. 32, 1926.) Single copy of the chart can be furnished at a cost of $ .50.
19
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
r r
Wj Ib. Water Vapor
1 Ib. Dry Air
V^ Ib. Water Vapor
1 )b. Dry Air
2 \ 2
(W3~Wi)to. Water
FIG. 1. DIAGRAM ILLUSTRATING ENERGY EQUATION 15
pound of dry air for saturation, the grains of moisture per cubic foot of
saturated air, the total heat in Btu per pound of dry air saturated with
moisture, and the weight of the dry air in pounds per cubic foot. ^ Fig.^2
shows the procedure to follow in using the Bulkeley Chart. The directrix
curves above the saturation line are as follows:
A is the total heat in Btu contained in the mixture above 0 F, and is to be referred
to the column of figures at the left side of the chart. Heat of the liquid is not included.
B is the grains of moisture of water vapor contained in each pound of the saturated
mixture and is to be referred to the figures at the left side of the chart.
C is the grains of moisture of water vapor per cubic foot of saturated mixture, and is
to be referred to the figures at the left side of the chart which are to be divided by 10.
D Is the weight in decimal fractions of a pound, of one cubic foot of the saturated
mixture, and is referred to the first column of figures to the right of the saturation line
between the vertical dry-bulb temperature lines 170 and 180 F. The relative density of
AB-C-D-E* Directrix Lines
D,aL'Dry Bulb line
D. P. Lc Dew Point Line
6.P.LB.=Grains Moisture perLb.Drv AirSahiraM
T.H.»Totel Heat per Lb.Dry Air Saturated
V.P.= Vapor Pressure in Mm. Mercury
6.RCF.S =6roins Moisture per Cu.Ft Saturated Air
R.H.L=Relative Humidity Line
W.Bl,»WetBulbUne
S.L" Saturation Ung
WJ>C£i=l%TtperCu.Ft,in Lbs.Saturated
R-D.S.'Relative Density perCu.F-r.Saturcrted
WP.CF.O.«Retofive Dererty per Cu.Fr.Dry
R.D.D.=RetfltiveDensfryperCu.Ft.Ory
6 P r F x Abs.Temp.gt P.P. .
U Abs.Temp.crtD.B."
-Abs.Temp.crt a P. .
Abs.Temp,atD.B.
R n y Abs.Temp.a+P.P.s
AbsJemp.atD.B.
*G.P.C.F at Partial Saturation
W.P.C.F at Partial Saturation
R.D. at Partial Saturation
FIG. 2. DIAGRAMS SHOWING PROCEDURE TO FOLLOW IN USING BULKELEY CHART
20
CHAPTER 1 — FUNDAMENTALS OF HEATING AND AIR CONDITIONING
the mixture is read in a similar manner from the same curve by the column of figures
between the vertical dry-bulb temperature lines 180 and 190 F.
E is similar to D but is for dry air, devoid of all moisture or water vapor. For con-
venience, the approximate absolute temperature of 500 F is given at 40 F on the satura-
tion line for the purpose of calculating volume, weight per cubic foot, and relative density
at partial saturation.
METHOD OF USING THE CHART
Example 8. Relative Humidity: At the intersection of the 78 F wet-bulb line and the
95 F dry-bulb line, the relative humidity is read directly on the straight diagonal lines
as 46 per cent.
Example 9. Dew Point: At the intersection of the 78 F wet-bulb line, the dew-point
temperature is read directly on the horizontal temperature lines as 70.9 F.
Example 10. Vapor Pressure: At the intersection of the 78 F wet-bulb line and the
95 F dry-bulb line, pass in a horizontal direction to the left of the chart and on the
logarithmic scale read the vapor pressure as 19.4 millimeters of mercury. (Divide by
25.4 for inches.)
Example 11. Total Heat Above 0 F in Mixture per Pou?id of Dry Air Saturated with
Moisture: From where the wet-bulb line joins the saturation line, pass in a vertical
direction on the 78 F dry-bulb line to its intersection with curve A and on the logarithmic
scale at the left of the chart read 40.6* Btu per pound of mixture. The use of this curve
to obtain the total heat in the mixture at any wet-bulb temperature is a great con-
venience, as the number of Btu required to heat the mixture and humidify it, as well as
the refrigeration required to cool and dehumidify the mixture, can be obtained by
taking the difference in total heat before and after treatment of the mixture.
Example 12. Grains of Moisture per Pound of Mixture: From 70.9 F dew-point
temperature on the saturation line, pass vertically to the intersection with curve B and
on the logarithmic scale at the left read 114 grains of moisture per pound.
Example 18. Grains of Moisture per Cubic Foot of Mixture, Partially Saturated: From
70.9 F dew-point temperature on the saturation line proceed in a vertical direction to
curve C, and on the logarithmic scale to the left read 83.3 which, divided by 10, gives
8.33 grains. A temperature of 70.9 F is equal to an absolute temperature of 530.9, and
530 9
95 F equals 555, absolute temperature. Therefore, K ' X 8.33 = 7.97 grains per
ooo
cubic foot of partially saturated mixture.
Example 14- Grains of Moisture per Cubic Foot of Dry Air, Saturated: Starting at the
saturation line at the desired temperature, pass in a vertical direction to curve C and on
the logarithmic scale at the left, read a number which, divided by 10, will give the
answer.
Example 15. Weight per Cubic Foot of Dry Air and Relative Density: From the point
where, for example, die 70 F vertical dry-bulb line intersects curve E, pass to right side
and read 0.075 Ib ; if cubic feet per pound are desired, divide 1 by this amount. The
relative density is read immediately to the right as 1.00.
Example 16. Weight per Cubic Foot of Saturated Air and Relative Density: From the
point where, for example, the 70 F vertical line intersects the curve D, pass to the right
and read weight per cubic foot as 0.07316 with a relative density of 0.9755 for saturated
air at 70 F.
Example 17. Weight per Cubic Foot and Relative Density of Partially Saturated Air:
Air at 50 F and a wet-bulb temperature of 46 F is to be heated to 130 F. The wet- and
dry-bulb lines intersect at a dew-point temperature of 42 F. Pass to the left where this
dew-point line intersects the saturation line and then pass in a vertical direction to where
the 42 F dry-bulb line intersects with curve D. Then pass directly to the right and read
the weight per cubic foot of saturated air at 42 F as 0.07844 and the relative density as
1.046. The absolute temperature at 42 F is 502, and at 130 F is 590. Therefore,
CAO
*j~ « 0.851. The weight of 1 cu ft of air at 50 F dry-bulb and 46 F wet-bulb when
heated to 130 F is 0.07844 X 0.851 = 0.06675, and the relative density is 1.046 X 0.851
= 0.89.
21
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
PROPERTIES OF STEAM
Steam is water vapor which exists in the vaporous condition because
sufficient heat has been added to the water to supply the latent heat of
evaporation and change the liquid into vapor. This change in state takes
place at a definite and constant temperature which is determined solely
by the pressure of the steam. The volume of a pound of steam is the
specific wlume which decreases as the pressure increases. The reciprocal
of this, or the weight of steam per cubic foot, is the density. (See Table 7.)
Steam which is in contact with the water from which it was generated is
known as saturated steam. If it contains no actual water in the form of
mist or priming, it is called dry saturated steam. If this be heated and the
pressure maintained the same as when it was vaporized, its temperature
will increase and it will become superheated, that is, its temperature will
be higher than that of saturated steam at the same pressure.
PROPERTIES OF WATER
Composition of Water. Water is a chemical compound (H20) formed by
the union of two volumes of hydrogen and one volume of oxygen, or two
parts by weight of hydrogen and 16 parts by weight of oxygen.
Density of Water. Water has its greatest density at 39.2 F, and it
expands when heated or cooled from this temperature. At 62 F a U. S.
gallon of 231 cu in. of water weighs approximately 8J^ Ib, and a cubic foot
of water is equal to 7.48 gal. The specific volume of water depends on the
temperature and it is always the reciprocal of its density. (See Table 8.)
Water Pressures. Pressures are often stated in feet or inches of water
column. At 62 F, with h equal to the head in feet, the pressure of a
column of water is 62.3S3& Ib per square foot, or 0.433& Ib per square inch.
A column of water 2.309 ft (27.71 in.) high exerts a pressure of one pound
per square inch at 62 F.
Boiling Point of Water. The boiling point of water varies with the
pressure; it is lower at higher altitudes. A change in pressure will always
be accompanied by a change in the boiling point, and there will be a cor-
responding change in the latent heat of evaporation. These values are
given in Table 7.
Specific Heat. The specific heat of water, or the amount of heat (Btu)
required to raise the temperature of one pound of water one degree Fahren-
heit, varies with the temperature, but it is commonly assumed to be
unity at all temperatures. Steam tables are based on exact values,
however. The specific heat of ice at 32 F is 0.492 Btu per pound. The
amount of heat required to raise one pound of water at 32 F through a
known temperature interval depends on the average specific heat for the
temperature range.
Sensible and Latent Heat. The heat necessary to raise the temperature
of one pound of water from 32 F to the boiling point is known as the heat
of the liquid or sensible heat. When more heat is added, the water begins
to evaporate and expand at constant temperature until the water is
entirely changed into steam. The heat thus added is known as the latent
heat of evaporation.
22
CHAPTER 1 — FUNDAMENTALS OF HEATING AND AIR CONDITIONING
TABLE
Abt. Pres*. Temp.
7. PROPERTIES OF SATURATED STEAM: PRESSURE TABLE**
Specific Volume Total Heat Entropy
Sat. Sat. Sat. Sat. Sat. Sat. Ab«. Pre**.
Lb./Sq. In. Deg. F.
Liquid
Evap.
Vapor
Liquid
Evap.
Vapor
Liquid
Evap.
Vapor Lb./Sq. In.
^P
t
Vf
Vfg
Vg
hf
hfg
kg
Sf
Sfg
Sg
P
58.83
0.01603
1256.9 1
,256.9
26.88
1058.8
1085.7
0.0533
2.0422
2.0955
V&" &£
3 / n gw
70.44
0.01605
856.5
856.5
38.47
1052.5
1091.0
0.0754
1.9856
2.0609
3/4" Hg
r'Hg
79.06
0.01607
652.7
652.7
47.06
1047.8
1094.9
0.0914
1.9451
2.0365
l"Hg
91.75
0.01610
4453
4453
59.72
1040.8
1100.6
0.1147
1.8877
2.0024
iVi" s&
2"Hg
101.17
0.01613
339.5
339.5
69.10
1035.7
1104.S
0.1316
1.846S
1.9784
2"Hg
2W' Hg
108.73
0.01616
275.2
2752
76.63
1031.5
1108.1
0.1450
1.8148
1.9598
2V2"Hg
3"Hg
115.08
0.01618
231.8
231.8
82.96
1027.9
1110.8
0.1551
1.7885
1.9446
3"Hg
1.0
101.76
0.01614
333.8
333.9
69.69
10353
1105.0
0.1326
1.8442
1.9769
1.0
2.0
126.10
0.01623
173.94
173.96
93.97
1021.6
1115.6
0.1750
1.7442
1.9192
2.0
3.0
141.49
0.01630
118,84
118.86
10933
1012.7
1122.0
0.2009
1.6847
1.8856
3.0
4.0
152.99
0.01636
90.72
90.74
120.83
1005.9
1126.8
0.2198
1.6420
1.8618
4.0
5.0
162.25
0.01641
73.59
73.61
130.10
1000.4
1130.6
0.2348
1.6088
1.8435
5.0
6.0
170.07
0.01645
62.03
62.05
137.92
995.8
1133.7
0.2473
1.5814
1.8287
6.0
7.0
176.85
0.01649
53.68
53.70
144.71
991.7
1136.4
0.2580
1.5582
1.8162
7.0
8.0
182.87
0.01652
4738
4739
150.75
988.1
1138.9
0.2674
1.5379
1.8053
8.0
9.0
188.28
0.01656
42.42
42.44
156.19
984.8
1141.0
0.2758
1.5200
1.7958
9.0
10.0
193.21
0.01658
38.44
38.45
161.13
981.8
1143.0
0.2834
1.5040
1.7874
10.0
11.0
197.75
0.01661
35.15
35.17
165.68
979.1
1144.8
0.2903
1.4894
1.7797
11.0
12.0
201.96
0.01664
32.40
3Z.42
169.91
976.5
1146.4
0.2968
1.4760
1.7727
12.0
13.0
205.88
0.01666
30.06
30.08
173.85
974.1
1147.9
0.3027
1.4636
1.7663
13.0
14.0
209.56
0.01669
28.05
28.06
177.55
971.8
11493
03082
1.4521
1.7604
14.0
14.696
212.00
0.01670
26,80
26.82
180.00
970.2
1150.2
03119
1,4446
1.7564
14.696
16.0
21632
0.01673
24.75
24.76
18435
967.4
1151.8
03184
1.4312
1.7496
16.0
18.0
222.40
0.01678
22.16
22.18
190.48
963.5
1154.0
03274
1.4127
1.7402
18.0
20.0
227.96
0.01682
20.078
20.095
196.09
959.9
1155.0
03356
13960
1.7317
20.0
22.0
233.07
0.01685
18363
18380
201.25
956.6
1157.8
03431
13809
1.7240
22.0
24.0
237.82
0.01689
16.924
16.941
206.05
953.4
1159.5
03500
13670
1.7170
24.0
26.0
242.25
0.01692
15.701
15.718
210.54
950.4
1161.0
J03564
13542
1.7106
26.0
28.0
246.41
0.01695
14.647
14.664
214.75
947.7
1162.4
03624
13422
1.7046
28.0
30.0
25034
0.01698
13.728
13.745
218.73
945.0
1163.7
03680
13310
1.6990
30.0
32.0
254.05
0.01701
12.923
12.940
222.50
942.5
1165.0
03732
13206
1.6938
32.0
34.0
257.58
0.01704
12.209
12.226
226.09
940.0
1166.1
03783
13107
1.6890
34.0
36.0
260.94
0.01707
11.570
11.587
229.51
937.7
1167.2
03830
13014
1.6844
36.0
38.0
264.16
0.01710
10.998
11.015
232.79
935.5
11683
03876
1.2925
1.6800
38.0
40.0
267.24
0.01712
10.480
10.497
235.93
9333
1169.2
03919
1.2840
1.6759
40.0
42.0
270.21
0.01715
10.010
10.027
238.95
931.2
1170.2
03961
1.2759
1.6720
42.0
44.0
273.06
0.01717
• 9.582
9.599
241.86
929.2
1171.1
0.4000
1.2682
1.6683
44.0
46.0
275.81
0.01719
9.189
9.207
244.67
9272
1171.9
0.4039
1.2608
1.6647
46.0
48.0
278.45
0.01722
8.829
8.846
24737
925.4
1172.7
0.4076
1.2537
1.6613
48.0
50.0
281.01
0.01724
8.496
8.514
249.98
923.5
1173.5
0.4111
1.2469
1.6580
60.0
52.0
283.49
0.01726
8.189
8.206
252.52
921.7
11743
0.4145
1.2404
1.6549
62.0
54.0
285,90
0.01728
7.902
7.919
254.99
920.0
1175.0
0.4178
1.2340
1.6518
64.0
56.0
288.23
0.01730
7.636
7.653
25738
9183
1175.7
0.4210
1.2279
1.6489
66.0
58.0
290.50
0.01732
7388
7.405
259.71
916.6
1176.4
0.4241
1.2220
1,6461
68.0
60.0
292.71
0.01735
7.155
7.172
261.98
915,0
1177.0
0.4271
1.2162
1.6434
60.0
62.0
294.85-
0.01737
6.937
6.955
264.18
913.4
1177.6
0.4300
1.2107
1.6407
62.0
64.0
296.94
0.01739
6.732
6.749
26633
911.9
1178.2
0.4329
1.2053
1.6382
64.0
66.0
298.98
0.01741
6.539
6.556
268.43
910.4
1178.8
0.4356
1.2001
1.6357
66.0
68.0
300.98
0.01743
6357
6375
270.49
908.9
1179,4
0.4384
1.1950
1.6333
68.0
70.0
302.92
0.01744
6.186
6.203
272.49
907.4
1179.9
0.4410
1.1900
1.6310
70.0
72.0
304.82
0.01746
6.024
6.041
274.45
906.0
1180.5
0.4435
1.1852
1.6287
72.0
74.0
306.68
0.01748
5.870
5.887
27637
904.6
1181.0
0.4460
1.1805
1.6265
74.0
76.0
30830
0.01750
5.723
5.741
278.25
903.2
1181.5
0.4485
1.1759
1.6244
76.0
78.0
310.28
.0.01752
5.584
5.602
280.09
901.9
1182.0
0.4509
1.1714
1.6223
78.0
80.0
312.03
0.01754
5.452
5.470
281.90
900.5
1182.4
0.4532
1.1670
1.6202
80.0
82.0
313.74
0.01756
5325
5343
283.67
899.2
1182.9
0.4555
1.1627
1.6182
82.0
84.0
315.42
0.01757
5.204
5.222
285.42
897.9
1183.4
0.4578
1.1586
1.6163
84.0
86.0
317.06
0.01759
5.089
5.107
287.13
896.7
1183.8
0.4599
1.1545
1.6144
86.0
88.0
318.68
0.01761
4.979
4.997
288.80
895.4
1184.2
0-4621
1.1505
1.6126
88.0
90.0
320.27
0.01763
4.874
4.892
290.45
894.2
1184.6
0.4642
1.1465
1.6107
90.0
92.0
321.83
0.01764
4.773
4.791
292.07
893.0
1185.0
0.4663
1.1427
1.6090
92.0
94.0
32337
0.01766
4.676
'4.694
293.67
891.8
1185.4
0.4683
1.1389
1,6072
94.0
96.0
324.88
0.01768
4.584
4.602
•295.25
890.6
1185.8
0.4703
1.1352
1.6055
96.0
98.0
32637
0.01769
4-494
4.512
•JJ96.80
889.4
1186.2
0.4723
1.1316
1.6038
98.0
•Abstracted from Steam Tables and Mottier Diagram, by Prof. J. H. Keenan, 1930 edition, by permission
of the publisher, The American Society of Mechanical Engineers.
23
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 7. PROPERTIES OF SATURATED STEAM: PRESSURE TABLE — (Continued)
Specific Volume
Total Heat
Entropy
Abs. Press.
Temp.
Sat.
Sat.
Sat.
Sat.
Sat.
Sat.
Aba. Pr«ss.
Lb./Sq. In.
DC*.*-
Liquid
Evap.
Vapor
Liquid
Evap.
Vapor
Liquid
Evap.
Vapor
Lb./Sq. In.
P
t
Vf
Vfg
Vg
hf
hfg
he
Sf
Sfg
Sg
P
100.0
327.83
0.01771
4.408
4.426
29833
888.2
1186.6
0.4742
1.1280
1.6022
100.0
102.0
329.27
0.01773
4326
4344
299.83
887.1
1186.9
0.4761
1.1245
1.6006
102.0
104.0
330.68
0.01774
4.247
4.265
301.30
886.0
11873
0.4779
1.1211
1.5990
104.0
106.0
332.08
0.01776
4.171
4.189
302.76
884.9
1187.6
0.4798
1.1177
1.5974
106.0
108.0
333.44
0.01777
4.097
4.115
304.19
883.8
1188.0
0.4816
1.1144
1.5959
108.0
110.0
334.79
0.01779
4.026
4.044
305.61
882.7
11883
0.4834
1.1111
1.5944
110.0
112.0
336.12
0.01780
3.958
3.976
307.00
881.6
1188.6
0.4851
1.1079
1.5930
112.0
114.0
337.43
0.01782
3.892
3.910
308.36
880.6
1188.9
0.4868
1.1048
1.5915
114.0
116.0
338.72
0.01783
3.828
3.846
309.71
879.5
1189.2
0.4885
1.1017
1.5901
116.0
118.0
340.01
0.01785
3.766
3.784
311.05
878.5
1189.5
0.4901
1.0986
1.5887
118.0
120.0
341.26
0.01786
3.707
3.725
312.37
877.4
1189.8
0.4918
1.0956
1.5874
120.0
122.0
342.50
0.01788
3.652
3.670
313.67
876.4
1190.1
0.4934
1.0926
1.5860
122.0
124.0
343.73
0.01789
3.597
3.615
314.96
875.4
1190.4
0.4950
1.0897
1.5847
124.0
126.0
344.94
0.01791
3.542
3.560
316.23
874.4
1190.6
0.4965
1.0868
1.5834
126.0
128.0
346.14
0.01792
3.487
3.505
317.49
873.4
1190.9
0.4981
1.0840
1.5821
128.0
130.0
347.31
0.01794
3.433
3.451
318.73
872.4
1191.2
0.4996
1.0812
1.5808
130.0
132.0
348.48
0.01795
3.383
3.401
319.95
871.5
1191.4
0.5011
1.0784
1.5796
132.0
134.0
349.64
0.01796
3335
3353
321.17
870.5
1191.7
0.5026
1.0757
1.5783
134.0
136.0
350.78
0.01798
3.288
3306
32237
869.6
1191.9
0.5041
1.0730
1.5771
136.0
138.0
351.91
0.01799
3.242
3.260
323.56
868.6
1192.2
0.5056
1.0703
1.5759
138.0
140.0
353.03
0.01801
3.198
3.216
324.74
867.7
1192.4
0.5070
1.0677
1.5747
140.0
142.0
354.14
0.01802
3.155
3.173
325.91
.866.7
1192.6
0.5084
1.0651
1.5735
142.0
144.0
355.22
0.01804
3.112
3.130
327.06
865.8
1192.9
0.5098
1.0625
1.5724
144.0
146.0
35631
0.01805
3.071
3.089
328.20
864-9
1193.1
0.5112
1.0600
1.5712
146.0
148.0
357.37
0.01806
3.031
3.049
32932
864.0
11933
0.5126
1.0575
1.5701
148.0
150.0
358.43
0.01808
2.992
3.010
330.44
863.1
1193.5
0.5140
1.0550
1.5690
150.0
152.0
359.47
0.01809
2.954
2.972
331.54
862.2
1193.7
0.5153
1.0526
1.5679
152.0
154.0
360.51
0.01810
2.917
2.935
332.64
8613
1193.9
0.5166
1.0502
1.5668
154.0
156.0
361.53
0.01812
2.882
2.9QO
333.72
860.4
1194.1
0.5180
1.0478
1.5658
156.0
158.0
362.54
0.01813
2.846
2.864
334.80
859.5
11943
0.5193
1.0454
1.5647
158.0
160.0
363.55
0.01814
2.812
2.830
335.86
858.7
1194.5
0.5205
1.0431
1.5636
160.0
162.0
364.54
0.01816
2.779
2.797
336.91
857.8
1194.7
0.5218
1.0408
1.5626
162.0
164.0
365.52
0.01817
2.746
2.764
337.95
857.0
1194.9
0.5230
1.0385
1.5616
164.0
166.0
366.50
0.01818
2.715
2.733
338.99
856.1
1195.1
0.5243
1.0363
1.5606
166,0
168.0
367.46
0.01819
2.683
2.701
340.01
855.2
11953
0.5255
1.0340
1.5596
168.0
170.0
368.42
0.01821
2.653
2.671
341.03
854.4
1195.4
0.5268
1.0318
1.5586
170.0
172.0
369.37
0.01822
2.623
2.641
342.04
853.6
1195.6
0.5280
1.0296
1.5576
172.0
174.0
37031
0.01823
2.594
2.612
343.04
852.7
1195.8
0.5292
1.0275
1.5566
174.0
176.0
371.24
0.01825
2.566
2.584
344.03
851.9
1196.0
0.5304
1.0253
1.5557
176.0
178.0
372.16
0.01826
2.538
2.556
345.01
851.1
1196.1
0.5315
1.0232
1.5548
178.0
180.0
373.08
0.01827
2.511
2.529
345.99
850.3
1196.3
0.5327
1.0211
1.5538
180.0
182.0
374.00
0.01828
2.484
2.502
346.97
849.5
1196.4
0.5339
1.0190
1.5529
182.0
184.0
374.90
0.01829
2.458
2.476
347.94
848.6
1196.6
0.5350-
1.0169
1.5520
184.0
186.0
375.78
0.01831
2.433
2.451
348.89
847.9
1196.8
0.5362
1.0149
1.5511
186,0
188.0
376.67
0.01832
2.407
2.425
349.83
847.1
1196.9
0.5373
1.0129
1.5502
188.0
190.0
377.55
0.01833
2383
2.401
350.77
846.3
1197.0
0.5384
1.0109
1.5493
190.0
192.0
378.42
0.01834
2359
2377
351.70
845.5
1197.2
0.5395
1.0089
1.5484
192.0
194.0
379.27
0.01835
2335
2353
352.61
844.7
1197.3
0.5406
1.0070
1.5475
194.0
196.0
380.13
0.01837
2.312
2330
353.53
844.0
1197.5
0.5417
1.0050
1.5467
196.0
198.0
380.97
0.01838
2.289
2307
354.43
843.2
1197.6
0.5427
1.0031
1.5458
198.0
200.0
381.82
0.01839
2.267
2.285
35533
842.4
1197.8
0.5438
1.0012
1.5450
200.0
205.0
383.89
0.01842
2.213
2.231
357.56
840.5
1198.1
0.5465
0.9964
1.5429
205.0
210.0
385.93
0.01844
2.162
2.180
359.76
838.6
1198.4
0.5491
0.9918
1.5409
210.0
215.0
387.93
0.01847
2.113
2.131
361.91
836.8
1198.7
0.5516
0,9873
1.5389
215.0
220.0
389.89
0.01850
2.066
2.084
364.02
835.0
1199.0
0.5540
0.9829
1.5369
220.0
225.0
391.81
0.01853
2.0208
2.0393
366.10
833.2
1199.3
0.5565
0.9786
1.5350
225.0
230.0
393.70
0.01856
1.9778
1.9964
368.14
831.4
1199.6
0.5588
0.9743
1.5332
230.0
235.0
395.56
0.01859
1.9367
1.9553
370.15
829.7
1199.8
0.5612
0.9702
1.5313
235.0
240.0
397.40
0.01861
1.8970
1.9156
372.13
827.9
1200.1
0.5635
0,9661
1.5295
240.0
245.0
399.20
0.01864
1.8589
1.8775
374.09
826.2
1200,3
0,5658
0.9620
1.5278
245.0
24
CHAPTER 1 — FUNDAMENTALS OF HEATING AND AIR CONDITIONING
TABLE 7. PROPERTIES OF SATURATED STEAM:
PRESSURE TABLE — (Continued)
Specific Volume
Total Heat
Entropy
Abs. Press.
Lb./Sq. In.
Temp.
Dee. F.
Sat.
Liquid
Evap.
Sat.
Vapor
Sat.
Liquid
Evap.
Sat.
Vapor
Sat.
Liquid
Evap.
Sat.
Vapor
Abs. Press.
Lb./Sq. In.
P
t
Vf
VfK
Vg
hf
hfg
fcg
Sf
Sfg
sg
P
250.0
400.97
0.01867
1.8223
1.8410
376.02
824.5
1200.5
0.5680
0.9581
1.5261
250.0
260.0
404.43
0.01872
1.7536
1.7723
379.78
821.2
1201.0
0.5723
0.9504
1.5227
260.0
270.0
407.79
0.01877
1.6895
1.7083
383.44
818.0
1201.4
0.5765
0.9430
1.5194
270.0
280.0
411.06
0.01882
1.6302
1.6490
387.02
814.7
1201.8
0.5805
0.9357
1.5163
280.0
290.0
414.24
0.01887
1.5745
1.5934
390.50
811.6
1202.1
0.5845
0.9287
1.5132
290.0
300.0
41733
0.01892
1.5225
1.5414
393.90
808.5
1202.4
0.5883
0.9220
1.5102
300.0
320.0
423.29
0.01901
1.4279
1.4469
400.47
802.5
1203.0
0.5957
0.9089
1.5046
320.0
340.0
428.96
0.01910
13439
13630
406.75
796.6
1203.4
0.6027
0.8965
1.4992
340.0
360.0
434.39
0.01918
1.2689
1.2881
412.80
790.9
1203.7
0.6094
0.8846
1.4940
360.0
380.0
439.59
0.01927
1.2015
1.2208
418.61
7853
1203.9
0.6157
0.8733
1.4891
360.0
400.0
444.58
0.0194
1.1407
1.1601
424.2
779.8
1204.1
0.6218
0.8625
1.4843
400.0
420.0
44938
0.0194
1.0853
1.1047
429.6
774.5
1204.1
0.6277
0.8520
1.4798
420.0
440.0
454.01
0.0195
1.0345
1.0540
434.8
7693
1204.1
0.6334
0.8420
1.4753
440.0
460.0
458.48
0.0196
0.9881
1.0077
439.9
764.1
1204.0
0.6388
0.8322
1.4711
460.0
480.0
462.80
0.0197
0.9456
0.9633
444.9
759.0
1203.9
0.6441
0.8228
1.4670
480.0
600.0
466.99
0.0198
0.9063
0.9261
449.7
754.0
1203.7
0.6493
0.8137
1.4630
500.0
520.0
471.05
0.0198
0.8701
0.8899
454.4
749.0
1203.5
0.6543
0.8048
1.4591
520.0
640.0
474.99
0.0199
0.8363
0.8562
459.0
744.1
1203.2
0.6592
0.7962
1.4554
540.0
560.0
478.82
0.0200
0.8047
0.8247
463.6
7393
1202.9
0.6639
0.7878
1.4517
560.0
680.0
482.55
0.0201
0.7751
0.7952
468.0
734.5
1202.5
0.6686
0.7796
1.4482
580.0
600.0
486.17
0.0202
0.7475
0.7677
4723
729.8
1202.1
0.6731
0.7716
1.4447
600.0
620.0
489.71
0.0202
0.7217
0.7419
476.6
725.1
1201.7
0.6775
0.7638
1.4413
620.0
640.0
493.16
0.0203
0.6972
0.7175
480.8
720.5
1201.2
0.6818
0.7562
1.4380
640.0
660.0
496.53
0.0204
0.6744
0.6948
484.9
715.9
1200.8
0.6861
0.7487
1.4348
660.0
680.0
499.82
0.0205
0.6527
0.6732
488.9
7113
1200.2
0.6902
0.7414
1.4316
680.0
700.0
503.04
0.6206
0.6321
0.6527
492.9
706.8
1199.7
0.6943
0.7342
1.4285
700.0
720.0
506.19
0.0206
0.6128
0.6334
496.8
702.4
1199.2
0.6983
0.7272
1.4255
720.0
740.0
509.28
0.0207
0.5944
0.6151
500.6
697.9
1198.6
0.7022
0.7203
1.4225
740.0
760.0
51230
0.0208
0.5769
0.5977
504.4
693.5
1198.0
0.7060
0.7136
1.4196
760.0
780.0
515.27
0.0209
0.5602
0.5811
508.2
689.2
1197.4
0.7098
0.7069
1.4167
780.0
SOO.O
518.18
0.0209
0.5444
0.5653
511.8
684.9
1196.7
0.7135
0.7004
1.4139
800.0
820.0
521.03
0.0210
0.5293
0.5503
515.5
680.6
1196.0
0.7171
0.6940
1.4111
820.0
840.0
523.83
0.0211
0.5149
0.5360
519.0
676.4
1195.4
0.7207
0.6877
1.4084
840.0
860.0
526.58
0.0212
0.5013
0.5225
522.6
672.1
1194.7
0.7242
0.6815
1.4057
860.0
880.0
529.29
0.0213
0.4881
0.5094
526.0
667.9
1194.0
0.7277
0.6754
1.4031
880.0
900.0
531.95
0.0213
0.4756
0.4969
529.5
663.8
11933
0.7311
0,6694
1.4005
900.0
920.0
534.56
0.0214
0.4635
0.4849
532.9
659.7
1192.6
0.7344
0.6635
13980
920.0
940.0
537.13
0.0215
0.4520
0.4735
536.2
655.6
1191.8
0.7377
0.6577
13954
940.0
960.0
539.66
0.0216
0.4409
0.4625
539.6
651.5
1191.1
0.7410
0.6520
13930
960.0
980.0
542.14
0.0217
0.4303
0.4520
542.8
647.5
11903
0.7442
0.6464
13905
980.0
1000.0
544.58
0.0217
0.4202
0.4419
546.0
643.5
1189.6
0.7473
0.6408
13881
1000.0
1050.0
550.53
0.0219
03960
0.4179
554.0
633.6
1187.6
0.7550
0.6273
13822
1050.0
1100.0
556.28
0.0222
03738
03960
561.7
623.9
1185.6
0.7624
0.6141
13765
1100.0
1150.0
561.81
0.0224
03540
03764
569.2
6143
11835
0.7695
0.6014
13709
1150.0
1200.0
567.14
0.0226
03356
03582
5763
604.9
1181.4
0.7764
0.5891
13656
1200.0
1250.0
57230
0.0228
03187
03415
583.6
595.6
1179.2
0.7831
0.5772
13603
1250.0
1300.0
57732
0.0230
03029
03259
590.6
5863
1177.0
0.7897
0.5654
13552
1300.0
1350.0
582.21
0.0232
0.2884
03116
597.5
577.2
1174.7
0.7962
0.5540
13501
1350.0
1400.0
586.96
0.0235
0.2748
0.2983
6043
568.1
1172.4
0.8024
0.5428
13452
1400.0
1450.0
591.58
0.0237
0.2621
0.2858
•611.0
559.1
1170.0
0.8086
0.5318
13404
1450.0
1500.0
596.08
0.0239
0.2502
0.2741
617.5
550.2
1167.6
0.8146
0.5212
13357
1600.0
1600.0
604.74
0.0244
0.2284
0.2528
630.2
532.6
1162.7
0.8262
0.5003
13265
1600.0
1700.0
612.98
0.0249
0.2089
0.2338
642.5
515.0
1157.5
0.8373
0.4801
13174
1700.0
1800.0
620,86
0.0254
0.1913
0.2167
654.7
497.2
115L8
0.8482
0.4601
13083
1800.0
1900.0
62839
0.0260
0.1754
0.2014
666.8
478,9
1145.7
0.8589
0.4402
1.2990
1900.0
2000.0
635.6
0.0265
0.1610
0.1875
679.0
460.0
1139.0
0.8696
0.4200
1.2896
2000.0
2200.0
649.2
0.0277
0.1346
0.1623
703.7
420.0
1123.8
0.8912
03788
1.2700
2200.0
2400.0
661.9
0.0292
o.im
0.1404
729.4
376.4
1105.8
0.9133
03356
1.2488
2400.0
2600.0
673.S
0.0310
0.0895
0.1205
756.7
327.8
1084.5
0.9364
0.2892
1.2257
2600.0
2800.0
684.9
0.0333
0.0688
0.1021
786.7
2723
1058.9
0.9618
0.2379
1.1996
2800.0
3000.0
695.2
0.0367
0.0477
0.0844
823.1
202.5
1025.6
0.9922
0.1754
1.1676
3000.0
3200.0
704.9
O.C459
0.0142
0.0601
887.0
75.9
962.9
1.0461
0.0651
1.1112
3200.0
3226.0
706,1
0.0522
0
0.0522
925.Q
0
925.0
1.0785
0
1.0785
3226.0
25
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
RATE OF EVAPORATION
In problems of air conditioning and drying, as well as in other industrial
applications of evaporation, such as cooling towers, it is desirable to
determine the rate of evaporation. There are two distinct cases of
evaporation. The first case is that in which the source of heat is primarily
from the water itself and in which the air temperature may even be raised.
TABLE 8. THERMAL PROPERTIES OF WATER
TEMPERATURE
DBG?
SAT. PRESS.
LB PER SQ IN.
VOLUME Cu FT
PERLB
WEIGHT LB PER
CuFT
SPECIFIC
HEAT
32
0.0887
0.01602
62.42
1.0093
40
0.1217
0.01602
62.42
1.0048
50
0.1780
0.01602
62.42
1.0015
60
0.2561
0.01603
62.38
0.9995
70
0.3628
0.01605
62.31
0.9982
80
0.5067
0.01607
62.23
0.9975
90
0.6980
0.01610
62.11
0.9971
100
0.9487
0.01613
62.00
0.9970
110
1.274
0.01616
61.88
0.9971
120
1.692
0.01620
61.73
0.9974
130
2.221
0.01625
61.54
0.9978
140
2.887
0.01629
61.39
0.9984
150
3.716
0.01634
61.20
0.9990
160
4.739
0.01639
61.01
0.9998
170
5.990
0.01645
60.79
1 .0007
180
7.510
0.01650
60.61
1.0017
190
9.336
0.01656
60.39
1.0028
200
11.525
0.01663
60.13
1.0039
210
14.123
0.01669
59.92
1.0052
212
14.696
0.01670
59.88
1.0055
220
17.188
0.01676
59.66
1.0068
240
24.97
0.01690
59.17
1.0104
260
35.43
0.01706
58.62
1.0148
280
49.20
0.01723
58.04
1.020
300
67.01
0.01742
57.41
1.026
350
134.62
0.01797
55.65
1.044
400
247.25
0.01865
53.62
1.067
450
422.61
0.0195
51.3
1.095
500
681.09
0.0205
48.8
1.130
550
1045.4
0.0219
45.7
1.200
600
1544.6
0.0241
41.5
1.362
700
3096.4
0.0394
25.4
The second is that in which the heat for evaporation is obtained entirely
from the air itself, in which case the air is cooled and the temperature oJ
the water remains substantially constant at the wet-bulb temperature
Both cases, however, may be reduced to a common basis of calculation
It has been found that the increase in the rate of evaporation is nearly ir
direct proportion to the increase in the air velocity, and that it is in dired
proportion to the difference in vapor pressure between the vapor pressure
of the water and the pressure of the vapor in the air.
26
CHAPTER 1 — FUNDAMENTALS OF HEATING AND AIR CONDITIONING
The general formula covering the experimental data may be expressed
as follows:
^ = (a + bu) («' - e) (17)
where
dw f
-j- = rate of evaporation.
a — the rate of evaporation in still air.
b — the rate of increase with velocity.
er = the vapor pressure of the liquid.
e = the vapor pressure in the atmosphere.
v = velocity.
The only difference between case one and case two is that in case
one the vapor pressure of the liquid is one of the known or assumed factors,
being dependent upon the known temperature of the liquid, while in
case two, e} is the vapor pressure corresponding to the wet-bulb tem-
perature of the air.
This wet-bulb or evaporation temperature is dependent upon the dry-
bulb temperature and the moisture content, or upon the total heat of the
air as indicated in the previous paragraph.
The effect of air velocity depends upon whether the flow of air is
parallel to the surface or perpendicular to the surface elements. For a
flow of air parallel to a horizontal surface
w = 0.093 ( 1 + ~Q ) («f — e) (approximately) (18)
where
w = pounds evaporated per square foot per hour.
v — velocity of atmosphere over surfaces, feet per minute.
e1 = vapor pressure of the water corresponding to its temperature.
e = vapor pressure in the surrounding atmosphere.
For transverse flow, as across a tubular surface, the rate of evaporation
is nearly doubled.
These relationships are indicated graphically on the chart, Fig. 3.
Since the difference in vapor pressures is substantially proportional to
the difference between the wet- and dry-bulb temperatures (i.e., the wet-
bulb depression) the rate of evaporation is also, for case two, substantially
proportionate to the wet-bulb depression.
In case two, the rate of sensible heat transfer from the air to the liquid
to produce evaporation is substantially the same as the rate of heat
transfer with the same type of surface, without moisture being present,
but with the same temperature differences. In other words, the rate of
heat transfer depends upon the temperature difference only, whether the
surface is wet or not. For example, it has been shown that the rate of
heat transfer with air flowing across staggered coils (transverse flow) may
be represented by the formula:
1
27
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
where
heat transfer expressed in Btu per hour per square foot per degree
difference in temperature between steam and air, for transverse flow.
At a velocity of 400 fpm, Ut « 5.8; at a velocity of 800 fpm, Ut = 9.3.
Referring to Fig. 3, showing the rate of heat transmission by evapo-
ration for different air velocities, it will be noted that for transverse flow
there are 560 Btu per hour per square foot transferred per inch difference
of vapor pressure at a velocity of 400 fpm, and 910 Btu per hour per square
foot per inch difference in vapor pressure at a velocity of 800 fpm. One
inch of vapor pressure difference corresponds approximately to 95 deg
difference between the wet- and dry-bulb temperature. Dividing by 95,
TT1 I11I8I1I1III1
FIG. 3. HEAT TRANSMITTED BY EVAPORATION
the value of 5.9 Btu per square foot per degree difference in temperature
is obtained for a velocity of 400 fpm, and 9.55 Btu per square foot for a
velocity of 800 fpm.
It will be noted that for these two cases the heat transfer by evapo-
ration per degree difference in temperature corresponds almost exactly
with the heat transfer by convection coils. The similarity may be noted
by comparing the formula for heat transfer in parallel flow, where
0.026
161
v
(20)
with the heat transfer by evaporation with parallel flow. The relationship
will be seen to be very close in both cases and would indicate that the heat
transfer by evaporation is actually brought about by a process of con-
vection.
28
CHAPTER 1 — FUNDAMENTALS OF HEATING AND AIR CONDITIONING
The difference in form of the two formulae may be due in part to
errors in observation at the higher and lower velocities.
In cooling air and condensing out the moisture therefrom the heat
transfer is considerably more rapid than when the air is dry and no
moisture is condensed. In general the rate of heat transmission on the
air side is increased an amount which is proportionate to the latent heat
removed as compared with the sensible heat removed. That is, if the
latent heat removed was 50 per cent of the sensible heat removed, then
the conductivity of the surface in contact with the air would be increased
approximately 50 per cent.
REFERENCES
A Review of Psychrometric Charts, by C. O. Mackey (Heating and Ventilating,
June, July, 1931).
A New Psychrometric Chart, by C. A. Bulkeley (A.S.H.V.E. TRANSACTIONS, Vol. 32,
1926).
Air Conditioning Applied to Cold Storage and a New Psychrometric Chart, by C. A.
Bulkeley (Refrigerating Engineering, February, 1932).
Air Conditioning Theory, by John A. Goff (Refrigerating Engineering, January, 1933).
Rational Psychrometric Formulae, by W.H. Carrier (A.S.M.E. Transactions, Vol. 33,
1911).
Temperature of Evaporation, by W. H. Carrier (A.S.H.V.E. TRANSACTIONS, Vol. 24,
1918).
Principles of Engineering Thermodynamics, by Kiefer and Stuart.
Basic Theory of Air Conditioning, by Lawrence Washington (Western Conference on
Air Conditioning, San Francisco, Calif., February 9-10, 1933).
Mixtures of Air and Water Vapor, by C. A. Bulkeley (Refrigerating Engineering,
January, 1933).
Temperature of Evaporation of Water into Air, by W. H. Carrier and D. C. Lindsay
(A.S.M.E. Transactions, 1924).
Chemical Engineering, by Lewis, Walker and McAdams.
Fan Engineering, Buffalo Forge Co.
The Psychrometric Chart, by E. V. Hill (Aerologist, April, May, June, 1932).
PROBLEMS IN PRACTICE
1 • Given air at 70 F dry -bulb and 50 per cent relative humidity with a baro-
metric pressure of 29.00 in. Hg, find the weight of vapor per pound of dry air.
Weight of saturated vapor per pound of dry air = Wt = 0.01578 Ib (Table 5). Satura-
tion pressure of the vapor at 70 F = et = 0.73S6 in. Hg.
From Equation 7r
0.01578 X 0.5 (29.00 - 0.7386)
29.00 - (0.5) (0.7386)
W = 0.00779 Ib of vapor per pound of dry air at 70 F dry-bulb and 50 per cent relative
humidity.
Approximate Method:
0.01578 X 0.5 = 0.00789 Ib of vapor per pound of dry air at 70 F dry-bulb and 50 per
cent relative humidity.
2 • Given air with a dry-bulb temperature of 80 F, relative humidity of 55 per
cent, and a barometric pressure of 29.92 in. Hg, calculate the weight of a cubic
foot of the mixture.
Weight of saturated vapor per cubic foot = 0.0015SO Ib (Table 5),
29
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
0.001580 X 0.55 = 0.000869 Ib = weight of vapor per cubic foot at 55 per cent relative
humidity.
Pressure of saturated vapor at 80 F = 1.0314 in. Hg.
Pressure of the vapor in the mixture = 1.0314 X 0.55 = 0.567 in. Hg.
Pressure of the dry air in the mixture = 29.92 - 0.567 == 29.353 in. Hg.
Weight of 1 cu ft of dry air at 80 F = -r^r- = 0.073529 Ib.
io.oU
2Q QCO
Weight of dry air in 1 cu ft of the mixture = 0.073529 X i^Sr = 0.072136 Ib.
/y.y^
0.072136 + 0.000869 = 0.073005 Ib - weight of 1 cu ft of the mixture.
3 • Given air with a dry-bulb temperature of 75 F, a relative humidity of 60 per
cent, and a barometric pressure of 29-92 in. Hg, calculate the volume of 1 Ib
of the mixture.
Weight of saturated vapor per cubic foot = 0.001352 Ib (Table 5).
0.001352 X 0.6 = 0.0008112 Ib = weight of vapor per cubic foot at 60 per cent relative
humidity.
Pressure of saturated vapor at 75 F = 0.8744 in. Hg.
Pressure of vapor in the mixture = 0.8744 X 0.6 ** 0.525 in. Hg.
Pressure of dry air in the mixture = 29.92 - 0.525 = 29.395 in. Hg.
Volume of 1 Ib of dry air at 75 F = 13.48 cu ft.
on QO
Volume of 1 Ib of dry air in the mixture =* 13.48 X OA onc. = 13.72 cu ft.
,&y.oyo
Weight of dry air in 1 cu ft of the mixture = lV,0 = 0.072886 Ib.
Lo,t A
0.072886 + 0.000811 « 0.073697 Ib » weight of 1 cu ft of the mixture.
A A»7oafV7 ~ 13.57 cu ft = volume of 1 Ib of the mixture.
i/.u/ooy/
Approximate Method:
Volume of 1 Ib of saturated air at 75 F « 13.88 cu ft.
Volume of 1 Ib of dry air at 75 F = 13.48 cu ft.
Difference in volume = 0.40 cu ft.
Relative humidity - 60 per cent.
0.40 X 0.6 = 0.24 cu ft.
13.48 + 0.24 = 13.72 cu ft « volume of 1 Ib of the mixture.
The degree of approximation is evident.
4 • Given saturated air at a temperature of 75 F and a barometric pressure of
29.92 in. Hg, determine the total heat of the mixture per pound of dry air.
From Equation 11 and Table 5,
Cpa = mean specific heat at constant pressure of dry air = 0.24.
. feg = latent heat of vaporization at the wet-bulb temperature == 1050.1 Btu per Ib.
W<L = weight of water vapor mixed with each pound of dry air = 0.01877 Ib.
2 = 0.24 (75 - 0) + (0.01877) (1050.1).
S = 37.71 Btu per Ib of dry air.
5 • Given ah* at 85 F dry-bulb temperature, 75 F wet-bulb temperature, and a
barometric pressure of 29.92 in. Hg; determine the total heat of the mixture
per pound of dry air.
From Equation 10 and Table 5,
CPa = 0.24.
Affg = 1050.1 Btu.
30
CHAPTER 1 — FUNDAMENTALS OF HEATING AND AIR CONDITIONING
Relative humidity = 62.3 per cent (from psychro metric chart).
W = 0.02634 X 0.623 = 0.01641 grains of moisture per Ib of dry air.
S = 0.24 (85 - 0) -f 0.01641 [1050.1 -f 0.45 fS5 - 75)].
2 = 37.71 Btu per pound of dry air.
It will be seen from Questions 4 and 5 that the total heat content is a function of the
wet-bulb temperature.
6 • It is desired to maintain a temperature of 80 F and a relative humidity of
50 per cent in a factory where the equipment gives off 6,000 Btu per hour. If
the entering air is at 70 F, determine the relative humidity, and the pounds of
air required per hour.
Air at 80 F and 50 per cent relative humidity contains 77 grains of moisture per pound.
At 70 F and 77 grains of moisture per pound, the relative humidity is 70 per cent.
Total heat above zero in the mixture at 80 F and 50 per cent relative humidity = 31.2
Btu per pound.
Total heat above zero in the mixture at 70 F and 70 per cent relative humidity = 28.8
Btu per pound.
31.2 - 28.8 = 2.4 Btu to be removed per pound of air.
6000 Btu = heat given off by equipment per hour.
6000
= 2500 Ib of air required per hour.
£A
7 • From the data given in Question 6, calculate the approximate cubic feet
of air required per minute.
Volume of 1 Ib of saturated air at 70 F = 13.69 cu ft (Table 5)
Volume of 1 Ib of dry air at 70 F = 13.35 cu ft.
Difference in volume = 0.34 cu ft.
Relative humidity = 70 per cent.
0.34 X 0.7 = 0.24 cu ft.
13.35 + 0.24 = 13.59 cu ft, volume of 1 Ib of mixture at 70 F and 70 per cent relative
humidity (approximate).
From Question 6 the air required per hour = 2500 Ib.
2500 X 13.59
60
566.25 cu ft per minute required.
8 • Given 1 Ib of dry air at 78 F and a barometric pressure of 29.92 in. Hg;
calculate the volume. If the temperature is raised to 96 F and the volume
remains constant, what will be the new pressure, P2, in in. Hg?
PV = WRT.
R (for air) = 53.34.
W = 1 Ib.
P — absolute pressure, pounds per square foot.
„ _ 1 X 53.34 X (78 + 460)
29.92 X 0.491 X 144
V = 13.57 cu ft = volume of 1 Ib.
PI rr z TI
(96 + 460) (29.92 X 0.491 X 144)
2 (78 -f 460) (0.491 X 144)
P2 » 30.90 in. Hg. -
31
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
9 • Given saturated air at a temperature of 75 F and a barometric pressure of
29.92 in. Hg; determine the heat content of the mixture per pound of dry air,
including the heat content of the liquid above 32 F.
From Equation 12,
/; = 0.24 (/ - 0) + W (1059.2 -f 0.450-
where
hs = 1059.2 -f 0.45/ (Empirical equation derived from Keenan's Steam Tables.)
/ = 75 F.
II' = 0.01S77 Ib of water vapor (Table 5).
h - 0.24 (75 - 0) -|- 0.01877 (1059.2 4- 0.45 X 75).
h = 38.51 Btu per pound of dry air.
Chapter 2
VENTILATION
AND AIR CONDITIONING STANDARDS
litiation of Air, Heat Regulation in Man, Effects of Heat,
Effects of Cold, Temperature Changes, Acclimatization,
W'armth and Comfort, Effective Temperature, Comfort Chart,
Comfort Line, Comfort Zone, Application of Comfort Chart,
A.S.H.V.E. Ventilation Standards, Natural and Mechanical
Ventilation, Recirculation, Ultra-Violet Radiation and lonisa-
tion, Heat and Moisture Losses
VENTILATION is defined in part as "the process of supplying or
removing air by natural or mechanical means to or from any space."
(See Chapter 41.) The word in itself implies quantity but not necessarily
quality. From the standpoint of comfort and health, however, the
problem is now considered to be one of securing air of the proper quality
rather than of supplying a given quantity.
The term air conditioning in its broadest sense implies control of any or
all of the physical or chemical qualities of the air. More particularly, it
includes the simultaneous control of temperature, humidity, movement,
and purity of the air. The term is broad enough to embrace whatever
other additional factors may be found desirable for maintaining the
atmosphere of occupied spaces at a condition best suited to the physio-
logical requirements of the human body.
VITIATION OF AIR
Under the artificial conditions of indoor life, the air undergoes certain
physical and chemical changes which are brought about by the occupants
themselves. The oxygen content is somewhat reduced, and the carbon
dioxide slightly increased by the respiratory processes. Organic matter,
which is usually perceived as odors, comes from the nose, mouth, skin
and clothing. The temperature of the air is increased by the metabolic
processes, and the humidity raised by the moisture emitted from the skin
and lungs. Moreover, according to latest researches1, there is a marked
decrease in both positive and negative ions in the air of occupied rooms.
Contrary to old theories, the usual changes in oxygen and carbon
dioxide are of no physiological concern because they are much too small
even under the worst conditions. The amount of carbon dioxide in air is
often used in ventilation work as an index of odors of human origin, but
*See A.S.H.V.E. research paper entitled Changes in Ionic Content in Occupied Rooms Ventilated by
Natural and Mechanical Methods, by C. P. Yaglou, L. C. Benjamin and S. P. Choate (A.S.H.V.E, TRANS-
ACTIONS, Vol. 37, 1931).
33
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
the information it affords rarely justifies the labor involved in making the
observation2. Little is known of the identity and physiological effects of
the organic matter given off in the process of respiration. The former
belief that the discomfort experienced in confined spaces was due to some
toxic volatile matter in the expired air is now limited, in the light of
numerous researches, to the much less dogmatic view that the presence of
such a substance has not been demonstrated. The only certain fact is
that expired and transpired air is odorous and offensive, and it is capable
of producing loss of appetite and a disinclination for physical activity.
These reasons alone, whether aesthetic or physiological, are sufficient to
warrant a desire for proper air conditions.
A certain part of the dissemination of disease which occurs in confined
spaces is caused by the emission of pathogenic bacteria from infected
persons. Infections by droplets from coughing and sneezing constitute a
limited mode of transmission in the immediate vicinity of the infected
person. Experiments have shown that the mouth spray is a coarse rain
which settles down quickly. The contamination is local and the problem
is considered to be largely one of contact infection rather than air-borne
infection.
The primary factors in air conditioning work, in ^the absence of any
specific contaminating source, are temperature, humidity, air movement
and body odors. As compared with these physical factors, the chemical
factors are, as a general rule, of secondary importance.
HEAT REGULATION IN MAN
The importance of temperature, humidity and air movement arises
from the profound influence which these factors exert upon body tem-
perature, comfort and health. Body temperature is a resultant of the
balancing action between its heat production and its heat loss. ^ The heat
resulting from the combustion of food within the body maintains its
temperature well above that of the surrounding air. At the same time,
heat is constantly lost from the body by radiation, conduction and
evaporation. Since, under ordinary conditions, the body temperature is
maintained at its normal level of about 98.6 F, the heat production must
be balanced by the heat loss. In healthy persons this takes place auto-
matically by the action of the heat regulating mechanism.
According to the general view, special areas in the skin are sensitive to
temperature. Nerve courses carry the sense impressions to the brain and
the response comes back over another set of nerves, the motor nerves, to
the musculature and to all the active tissues in the body, including the
endocrine glands. In this way, a two-sided mechanism controls the body
temperature by (1) regulation of internal heat production (chemical
regulation), and (2) regulation of heat loss by means of automatic varia-
tion in the rate of cutaneous circulation and the operation of the sweat
glands (physical regulation). The mechanisms of adjustment are complex
and little understood at the present time. Coordination of these dif-
ferent mechanisms seems to vary greatly with different air conditions.
'Indices of Air Change and Air Distribution, by F. C. Houghten and J. L. Blackshaw (A.S.H.V.E.
Journal Section, Heating, Piping and Air Conditioning, June, 1933, p. 324).
CHAPTER 2 — VENTILATION AND AIR CONDITIONING STANDARDS
With rising air temperatures up to 75 F or 80 F, metabolism, or internal
heat production, is decreased3, probably by an inhibitory7 action on heat
producing organs, especially the adrenal glands, which seem to exert the
major influence on basic combustion processes in the body. The blood
capillaries in the skin become dilated by reflex action of the vasomotor
nerves, allowing more blood to flow into the skin, and thus increase its
temperature and consequently its heat loss. The increase in peripheral
circulation is at the expense of the internal organs. If this method of
cooling is not in itself sufficient, the stimulus is extended to the sweat
glands which allow water to pass through the surface of the skin, where it
is evaporated. This method of cooling is the most effective of all, as long
as the humidity of the air is sufficiently low to allow for evaporation. In
high humidities, where the difference between the dew-point temperature
of the air and body temperature is not sufficient to allow rapid evapora-
tion, equally good results may be obtained by increasing the air move-
ment, and hence the heat loss by conduction and evaporation.
In cold environments, in order to keep the body warm there is an actual
increase in metabolism brought about partly by voluntary muscular con-
tractions (shivering) and partly by an involuntary reflex upon the heat
producing organs. The surface blood vessels become constricted, and
the blood supply to the skin is curtailed by vasomotor shifts to the internal
organs in order to conserve body heat.
EFFECTS OF HEAT
Although the human organism is capable of adapting itself to variations
in environmental conditions, its ability to maintain heat equilibrium is
limited. The heat regulating center fails, for instance, if the external
temperature is so abnormally high that bodily heat cannot be eliminated
as fast as it is produced. Part of it is retained in the body, causing a rise
in skin and deep tissue temperature, an increase in the heart rate, and
accelerated respiration. (See Table 1.) In extreme conditions, the
metabolic rate is markedly increased owing to the excessive rise in body
temperature4, and a vicious cycle results which may eventually lead to
serious physiologic damage.
Examples of this are met with in unusually hot summer weather and in
hot industries where the radiant heat from hot objects renders heat loss
from the body by radiation and convection impossible. Consequently,
the workers depend entirely on evaporation for the elimination of body
heat. They stream with perspiration and drink liquids abundantly to
replace the loss.
One of the most deleterious effects of high temperatures is that the
blood is diverted from the internal organs to the surface capillaries, in
order to serve in the process of cooling. This affects the stomach, heart,
lungs and other vital organs, and it is believed that the feeling of lassitude
and discomfort experienced is due to the anaemic condition of the brain.
*Heat and Moisture Losses From the Human Body and Their Relation to Air Conditioning Problems*
by F. C. Houghten, W, W. Teague, W. E. Miller, and W. P. Yant (A.S.H.V.E, TRANSACTIONS, Vol. 35,
1929, p. 245).
*ThennaI Exchanges Between the Human Body and Its Atmospheric Environment, by F. C. Houghteiu
W. W. Teague, W. E. MUfer, and W. P. Yant {The American Journal of PJfcyswrfagy, Vol. 8&, No, £, April.
1929).
35
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 1. PHYSIOLOGICAL RESPONSES TO HEAT OF MEN AT REST AND AT \VoRKa
I ' j MEN AT WORK
ACTUAL
MEN A.T RE
ST
90,(
XX) FT-LB OF V
ORE PER HOU
R
EFFECTIVE
TEMP.
CHEEK
TEMP
(DEG
FAHR)
Rise in
Rectal
Temp
(Deg
Fahrper
Hour)
-
Increase
in Pulse
Rate
(Beats per
Mb per
Hour)
Approximate
Loss in Body
Weight by
Perspiration
(Lb perHr)
Total Work
Accomplished
(Ft-lb)
Rise in
Body Temp
(Deg Fahr
per Hr)
Increase in
Pulse Rate
(Beats per
Min per Hr)
Approximate
Loss in Body
Wt. by Per-
spiration (Lb
per Hr}
60
225,000
0.0
6
0.5
70
0.0
0
0.2
225,000
0.1
7
0.6
80
96.7
0.0
0
0.3
209,000
0.3
11
0.8
85
96.6
0.1
1
0.4
190,000
0.6
17
1.1
90
97.0
0.3
4
0.5
153,000
1.2
31
1.5
95
97.6
0.9
15
0.9
102,000
2.3
61
2.0
100
99.6
2.2
40
1.7
67,000
4.0
103b
2.7
105
104.7
4.0
83
2.7
49,000
6. Ob
158^
3.5b
110
5.9t»
137^
4. 0^
37,000
8.5b
237°
4.4*>
«Data by A.S.H.V.E. Research Laboratory.
bComputed va^e from exposures lasting less than one hour.
The stomach loses some of its power to act upon the food, owing to a
diminished secretion of gastric juice, and there is a corresponding loss in
the antiseptic and antifermentive action which favors the growth of
bacteria in the intestinal tract5. These are considered to be the potent
factors in the increased susceptibility to gastro-intestinal disorders in hot
summer weather. The vie fim may lose appetite and suffer from indiges-
tion, headache and general enervation, which may eventually lead to a
premature old age.
In warm atmospheres, particularly during physical work, a considerable
amount of chloride is lost from the system through sweating. The loss of
this substance may lead to attacks of cramps, unless the salts are replaced
in the drinking water. In order to relieve both cramps and fatigue,
Moss6 recommends the addition of 6 grams of sodium chloride and 4 grams
of potassium chloride to a gallon of water.
The deleterious physiologic effects of high temperatures exert a power-
ful influence upon physical activity, accidents, sickness and mortality.
Both laboratory and field data show clearly that physical work in warm
atmospheres is a great effort, and that production falls progressively as
the temperature rises. The incidence of industrial accidents reaches a
minimum at about 68 F, increasing above and below that temperature.
Sickness and mortality rates increase progressively as the temperature
rises.
EFFECTS OF COLD
The action of cold on human beings is not well known. Cold affects the
human organism in two ways: (1) through its action on the body as a
whole, and (2) through its action on the mucous membranes of the upper
respiratory tract. Little exact information is available on the latter.
On exposure to cold, the loss of heat is increased considerably and only
^Influence of Effective Temperature upon Bactericidal Action of Gasto-Intestinal Tract, by Arnold and
Brody (Proceedings Society Exp. Biol. Med. Vol. 24, 1927, p. 832).
6Some Effects of High Air Temperatures upon the" Miner, by K.'N. Moss (Transactions institute of
Mining Engineers, Vol. 66, 1924, p. 284).
36
CHAPTER 2 — VENTILATION AND AIR CONDITIONING STANDARDS
within certain limits is compensation possible by increased heat produc-
tion and decreased peripheral circulation. The rectal temperature often
rises upon exposure to cold but the pulse rate and skin temperature fall.
The blood pressure increases, owing to constriction in the peripheral
vessels and to thickening of the blood. The subcutaneous tissues and
muscles form reservoirs for storing the water which leaves the blood. In
extremely cold atmospheres compensation becomes inadequate. The
body temperature falls and the reflex irritability of the spinal cord is
markedly affected. The organism may finally pass into an unconscious
state which ends in death.
Cannon showed that excessive loss of heat is associated with increased
activity of the adrenal medulla7. The extra output of adrenin hastens
heat production which protects the organism against cooling. Bast8
found a degeneration of thyroid and adrenal glands upon exposure to cold.
Effects of Temperature Changes
A moderate amount of variability in temperature is known to be
beneficial to health, comfort, and the performance of physical and mental
work. On the other hand, extreme changes in temperature, such as those
experienced in passing from a warm room to the cold air out of doors,
appear to be harmful to the tissues of the nose and throat which are the
portals for the entry of respiratory diseases.
Experiments show that chilling causes a constriction of the blood
vessels of the palate, tonsils and throat, which is accompanied by a fall
in the temperature of the tissues. On rewarming, the palate and throat
do not always regain their normal temperature and blood supply. This
anaemic condition favors bacterial activity and it is believed to play a
part in the inception of the common cold and other respiratory diseases.
It is believed that the lowered resistance is due to a diminution in the
number and phagocytic activity ,of the leucocytes (white blood cells)
brought about by exposure to cold and by changes in temperature.
Sickness records in industries seem to strengthen this belief. The
Industrial Fatigue Research Board of England9 found that in workers
exposed to high temperatures and to changes in temperature, namely,
steel melters, puddlers, and tin-plate rnillmen, there is an excess of all
sickness, the excess among the puddlers being due chiefly to respiratory
diseases and rheumatism. The causative factor was not the heat itself
but the sudden changes in temperature to which the workers were exposed.
The tin-plate millmen who were not exposed to chills, since they work
almost continuously throughout the shift, had no excess of rheumatism
and respiratory diseases. On the other hand, the blast-furnacemen, who
work mostly in the open, showed more respiratory sickness than the steel
workers. This experience in British factories is well in accord with the
findings in American industries10. According to these data the highest
^Studies on the Condition of Activity of Endocrine Glands, by W. B. Cannon, A. Guerido,! S. W. Britton
and E. M. Bright (American Journal of Physiology, Vol. 79, 1926, p. 466).
8St tidies in Exhaustion Due to Lack of Sleep, by T. H. Bast, J. S. Supernaw, B. Lieberman and J. Munro
(American Journal of Physiology, Vol. 85, 1928, p, 135).
9Fatigue and Efficiency in the Iron and Steel Industry, by H. M. Veraon {Industrial Fatigue Research
Board, Report No. 5, 1920, London).
MIron Foundry Workers Show Highest Percentage of Deaths from Pneumonia {Statistical Bulletin,
Metropolitan Life Insurance Company, 1928).
37
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
pneumonia death rate is associated with dust, extreme heat, exposure to
cold, and to sudden changes in temperature.
ACCLIMATIZATION
Acclimatization and the factor of psychology are two important in-
fluences in air conditioning which cannot be ignored. The first is man's
ability to adapt himself to changes in air conditions; the second is an
intangible matter of habit and suggestion.
Some persons regard the unnecessary endurance of cold as a virtue.
They believe that the human organism can adapt itself to a wide range of
air conditions with no apparent discomfort or injury to health. In the
light of the present knowledge of air conditioning these views are not
justified. Acclimatization to extreme conditions involves a strain upon
the heat regulating system and it interferes with the normal physiologic
functions of the human body. Thousands of years in the heat of Africa
do not seem to have acclimatized the Negro to a temperature averaging
80 F. The same holds true of northern races with respect to cold, although
the effects are mitigated by artificial control. All this seems to indicate
that adaptation to a climate averaging between 60 and 80 F is a very
primitive trait11.
Within these limits, however, there does occur a definite adaptation to
external temperature level. People and animals raised under conditions
of tropical moist heat have a lower rate of heat production than do those
who grow up in cooler environments. This causes them to stand chilling
poorly as they are unable to quickly increase internal combustion to keep
up the body temperature. For this reason they have trouble standing
the cold, stormy weather of the temperate zones, and when exposed to it
are very susceptible to respiratory infections. Likewise, people living in
cool climates suffer greatly in the moist heat of the tropics until their
adrenal activity has slowed down. Within a couple of years, however,
they find themselves standing the heat much better and disliking cold.
They become acclimated by a definite change in the combustion level
within the body12.
In certain individuals the psychologic factor is more powerful than
acclimatization. A fresh air fiend may suffer in 3. room with windows
closed regardless of the quality of the air. As a matter of fact, instances
are known in which paid subjects refused to stay in a windowless but
properly conditioned experimental chamber because the atmosphere felt
suffocating to them upon entering the room.
WARMTH AND COMFORT
The temperature, humidity, and motion of the air, and the radiation
between a person and surrounding hot or cold surfaces, taken together,
determine his feeling of warmth and influence his elimination of body
heat. In other words, the temperature sensations of the human body
depend not only on the temperature of the surrounding air as registered
by a dry-bulb thermometer, but also upon the temperature indicated by
"Civilization and Climate, by Ellsworth Huntington, Yale University Press, 1924.
"Air Conditioning it its Relation to Human Welfare, by C. A. Mills, M.D. (A.S.H.V.E. Journal Section,
Heating, Piping and Air Conditioning, April, 1934).
38
CHAPTER 2 — VENTILATION AND AIR CONDITIONING STANDARDS
a wet-bulb thermometer. Dry air at a relatively high temperature may
feel cooler than air of considerably lower temperature with a high mois-
ture content. Air motion makes any moderate condition feel cooler.
On the other hand, in cold environments an increase in humidity
produces a cooler sensation. The dividing line at which humidity has no
effect upon comfort varies with the air velocity and is about 46 F (dry-
bulb) for still air and about 51, 56 and 59 F for air velocities of 100, 300
and 500 fpm, respectively.
Thermo- Equivalent Conditions
Combinations of temperature, humidity and air movement which pro-
duce the same feeling of warmth are called thermo-equivalent con-
ditions. A series of tests13' 14* 15 has been carried out in the psychrometric
rooms of the A.S.H.V.E. Research Laboratory, Pittsburgh, in order to
determine the equivalent conditions met with in general air conditioning
work. These show that this newly-developed scale of thermo-equivalent
conditions not only indicates the sensation of warmth, but also determines
the physiological effects on the body induced by heat and cold. " For this
reason, it is called the effective temperature scale or index.
Effective temperature is an index of warmth or cold. It is not in itself
an index of comfort, as it is often assumed to be, nor are the effective tem-
perature lines necessarily lines of equal comfort. This is true because, in
determining this index, the subjects compared not the relative comfort,
but rather the relative warmth or cold of various air conditions. Moist
air at a comparatively low temperature, and dry air at a higher tempera-
ture may each feel as warm as air of an intermediate temperature and
humidity, but the comfort experienced in the three air conditions would be
different, although the effective temperature is the same.
Under extreme humidity conditions there seems to be a difference be-
tween sensations of absolute comfort and of the proper degree of warmth.
In other words, human beings are not necessarily comfortable when the
air is neither too warm nor too cold. Air of proper warmth may, for in-
stance, contain excessive water vapor, and in this way interfere with the
normal physiologic loss of moisture from the skin, leading to damp skin
and clothing and producing more or less discomfort; or the air may be
excessively dry, producing appreciable discomfort to the mucous mem-
brane of the nose and to the skin which dries up and becomes chapped
from too rapid loss of moisture. According to the comfort experiments
first conducted at the A.S.H.V.E. Laboratory16 in the U. S. Bureau of
Mines, Pittsburgh, and later studies at the Harvard School of Public
Health17 in Boston, effective temperature appears to be a fair index of
comfort also, particularly within a humidity range of 30 to 60 per cent,
approximately.
"Determining Lines of Equal Comfort, by F. C. Houghteu and C. P. Yagloglou (A.S,H,V.E. TRANS-
ACTIONS, Vol. 29, 1923, p. 361).
"Cooling Effect on Human Beings by Various Air Velocities, by F. C. Houghten and C. P. Yaglogtou
(A.SwH.V.E. TRANSACTIONS, Vol. 30, 1924, p. 193),
"Effective Temperature with Clothing, by C. P. Yagloglou and W. E. Miller (A.S.H.V.E. TRANS-
ACTIONS, Vol. 31, 1925, p. 89).
^Determination of the Comfort Zone With Further Verification of Effective Temperatures Within This
Zone, by F. C. Houghten and C. P. Yaglogiou (A-S.H.V.E. TRANSACTIONS, Vol. 29, 1923, p. 361).
*rrhe Summer Comfort Zone; Climate and Clothing, by C, P. Yagloa and Philip Drinker
(A.S.H.V.E. TRANSACTIONS, Vot 35, 1959).
39
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
dJ
-aoo:
9
.705
FIG. 1. THERMOMETRIC OR EFFECTIVE TEMPERATURE CHART SHOWING NORMAL SCALE
. OF EFFECTIVE TEMPERATURE. APPLICABLE TO INHABITANTS OF THE
UNITED STATES UNDER FOLLOWING CONDITIONS:
A. Clothing: Customary indoor clothing. B. Activity: Sedentary or light muscular work. C. Heating
Methods: Convection type, «.«., warm air, direct steam or hot water radiators, plenum systems.
40
CHAPTER 2 — VENTILATION AND AIR CONDITIONING STANDARDS
Definition of Effective Temperature
Briefly, effective temperature may be defined as an arbitrary index of the
degree of warmth or cold felt by the human body in response to tempera-
ture, humidity, and movement of the air. Effective temperature is not a
true temperature of the air but an index which combines temperature,
humidity and air motion in a single value. The numerical value of the
effective temperature index for any given air condition is fixed by the
temperature of saturated air which, at a velocity or turbulence of 15 to
25 fpm, induces a sensation of warmth or cold like that of the given
condition. - Thus, any air condition has an effective temperature of
65 deg when it induces a sensation of warmth like that experienced in
practically still air at 65 F saturated with moisture.
In all reports of the A.S.H.V.E. Research Laboratory, the term still air
signifies the minimum air movement it was possible to obtain in the
Laboratory's psychrometric chamber. Actually, the air motion was
between 15 and 25 fpm in all experiments, without qualification, as
measured by the Kata thermometer. This was not a linear movement of
air but it represented the turbulence or eddy currents produced by the air
change. Even in tightly sealed rooms, the natural air movement is not
likely to fall below 10 fpm so long as there is a temperature or pressure
difference between the air inside and that outside the room.
Fig. 1 shows the results obtained at the A.S.H.V.E. Research Labora-
tory in a single chart, the so-called thermometric chart. The equivalent
conditions or effective temperature lines are shown by the short cross-
lines. The difference between the effective temperature for still air and
for moving air, of any velocity, represents the cooling resulting from that
air velocity. This thermometric chart applies to average normal and
healthy persons adapted to American living and working conditions. It
is limited to sedentary or light muscular activity, and to rooms heated by
the usual American convection methods (warm air, central fan and direct
hot water and steam heating systems) in which the difference between the
air and wall surface temperatures may not be great. The chart does not
apply to rooms heated by radiant methods such as the British panel
system, open coal fires, and the like. It will probably not apply with
adequate accuracy to races other than the white or perhaps to inhabi-
tants of other countries where the living conditions, climate, heating
methods, and clothing are materially different from those of the
subjects employed in experiments at the Research Laboratory.
If an occupant of a room loses heat by radiation to large wall or glass
surfaces at lower temperatures, the air within the room must be main-
tained at a higher temperature to compensate for this effect in order to
give the same feeling of warmth. The results of a recent study 1& by the
A.S.H.V.E. Laboratory, shown in Fig. 2, indicate that in po6rly insulated
buildings this effect may become of considerable importance. Thus an
occupant of a room having inside wall surface temperatures of 55 F on
three sides will require an air temperature of 7*4 F to have the same feeling
of warmth he would experience in at warm-wall room with air at 70 F. A
wall consisting of 8-in. brick and plaster, with 16 F outside air tenipera-
*8Cold Walls and Their Relation to the Feeling of Warmtfai by F. C; Hbtfefaffefc an^Pau! McDermott
(A.S.H.V.E. Journal Section, Heating, Piping and Air C&ndiiiomngt JaBtfeftv'ldSS; p: 53); ' - - . .
41
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
ture and 70 F inside air temperature, will have an inside surface tem-
perature of 55 F. The reverse effect will be experienced by occupants of
rooms having extensive high-temperature surfaces in them. In ^such
cases, a lower air temperature is required to compensate for heat radiated
to the occupant.
The effective temperature index for persons doing medium or heavy
muscular work, in still air, has also been determined at the A.S.H.V.E.
Research Laboratory19.
WALL TEMPERATURE DEC. FAHR.
FIG, 2. CORRECTION TO VARIOUS DRY-BULB TEMPERATURES IN A WARM- WALL ROOM
FOR THE SAME FEELING OF WARMTH IN ROOMS HAVING THREE COLD WALLS.
TEMPERATURES INDICATED BY SHIELDED THERMOMETERS 30 IN. ABOVE THE FLOOR
OPTIMUM AIR CONDITIONS
No single comfort standard can be laid down which would meet every
need. There is an inherent individual variation in the sensation of
warmth or comfort felt by persons when exposed to an identical atmos-
pheric condition. The state of health, age, sex, clothing, activity, and
the degree of acquired adaptation seem to be the important factors
affecting the comfort standards.
Since the prolonged effects of temperature, humidity and air move-
ment on health are not known to the same extent as their effects on com-
fort, the optimum conditions for health may not be identical with those
for comfort. On general physiologic grounds, however, the two do not
differ greatly since this is in accordance with the efficient operation of the
heat regulating mechanism of the body. This belief is strengthened by
^Effective Temperature for Persons Lightly Clothed and Working in Still Air, by F. C. Houghten.
W. W. Teague and W* E. Miller (A.S.H.V.E. TRANSACTIONS, Vol. 32, 1926).
42
CHAPTER 2 — VENTILATION AND AIR CONDITIONING STANDARDS
results of studies on premature infants over a four-year period20. By
adjusting the temperature and humidity so as to stabilize the body tem-
perature of these infants, the incidence of diarrhoea and mortality was
decreased, gains in body weight increased and infections were reduced
to a minimum.
Comfort Chart; Comfort Line; Comfort Zone
Fig. 3 shows a comfort chart, developed at the A.S.H.V.E. Laboratory,
on which the average and extreme comfort zones have been superimposed.
The extreme comfort zone includes air conditions in which one or more of
the experimental subjects were comfortable. The average comfort zone
includes those air conditions in which the majority of the subjects (50 per
cent or more) were comfortable. That particular effective temperature
at which the maximum number of subjects was comfortable was called
the comfort line.
The average winter comfort zone as determined at the A.S.H.V.E.
Laboratory ranges from 63 deg to 71 deg ET (effective temperature).
In winter while at rest, a large percentage of persons normally clothed
were found to be comfortable at 66 deg ET and this temperature has been
accepted by a committee of the Society21 as the winter comfort line or
optimum effective temperature.
The comfort line separates the cool air conditions to its left from the
warm air conditions to its right. Under the air conditions existing along
or defined by the comfort line, the body is able to maintain thermal
equilibrium with its environment with the least conscious sensation to the
individual, or with the minimum phsyiologic demand on the heat regulat-
ing mechanism. This environment involves not only the condition of the
air with respect to temperature and humidity, but also the condition of
the surrounding objects and wall surfaces. The comfort zone tests were
made in rooms with wall surface temperatures approximately the same as
the room dry-bulb temperature. For walls of large area having unusually
high or low surface temperatures, however, a somewhat lower or higher
range of effective temperature is required to compensate for the increased
gain or loss of heat to or from the body by radiation22.
The average summer comfort zone for exposures of 3 hours or more
ranges from about 66 deg to 75 deg ET, based on studies made at the
Harvard School of Public Health17. The probable optimum effective
temperature (for exposures of 3 hours or more) is 71 deg. These effective
temperatures average about 4 deg higher than those found in winter when
customary winter clothing was worn. The variation from winter to
summer is probably due partly to adaptation to seasonal weather and
partly to differences in the clothing worn in the two seasons.
The best effective temperature (for exposures lasting 3 hours or more)
was found to follow the average monthly outdoor temperature more
closely than the prevailing outdoor temperature. It remained at approxi-
»Applkation of Air Conditioning to Premature Nurseries in Hospitals, by C. P. Yagkra, Philip Drinker
and K. D. Blactfan (A.S.H.V.E. TRANSACTIONS, VoL 36, 1930).
»How to Use the Effective Temperature Index and Comfort Charts (A.S.H.V.E. TRANSACTIONS,
Vol. 38, 1932).
»CoM Walls and Their Relation to the Feeling of Warmth, by F. C. Houghten and Paul McDermott
(A.S.H.V.E. Jomnal Section, Hea&ng* Piping and Air Conditioning, January, 1933, p. 53).
43
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
90
Air Movement or Turbulence 15 to 25 ft. per mm.
Average Winter Comfort Zone — -
— ------ Average 'Winter Comfort Lme |
i','f,'f','\ Average Summer'Comfort Zone |
— — — «•• Average Summer Comfort Line
70 80
Pry Bulb Temperature F
FIG. 3. A.S.H.V.E. COMFORT CHART FOR AIR VELOCITIES OF 15 TO 25 FPM (STILL AiR)2L
Nate— Both summer and winter comfort zones apply to inhabitants of the United States only. Applica-
tion of winter comfort line is further limited to rooms heated by central station systems of the convection
type. The line does not apply to rooms heated by radiant methods. Application of summer comfort line
is limited to homes, offices and the like, where the occupants become fully adapted to the artificial air con-
ditions- The line does not apply to theaters, department stores, and the like where the exposure is less than
3 hours.
mately the same value in July, August and September, and although the
average monthly temperature did not vary much, the prevailing outdoor
temperature ranged from 70 F to 99.5 F. A decrease in the optimum
temperature became apparent only when the prevailing outdoor tempera-
ture fell to 66 F, which is below the customary room temperature in the
United States for summer and winter.
, Young men as a general rule prefer conditions in the cool region of the
comfort zone, and women, arid older people-, in the warm i region. of the
44
CHAPTER 2 — VENTILATION AND AIR CONDITIONING STANDARDS
comfort zone. Crowding the experimental chamber lowered the optimum
effective temperature from 70.8 deg when the gross floor area per occupant
was 44 sq ft and the air space 380 cu ft, to 69.4 deg when the floor area
was reduced to 14 sq ft and the air space to 120 cu ft per occupant.
In the comfort zone experiments of the A.S.H.V.E. Research Labora-
tory, the relative humidity was varied between the limits of 30 and 70 per
cent approximately, but the most comfortable range has not been deter-
mined. In similar experiments at the Harvard School of Public Health, a
relative humidity of 70 per cent was found to be somewhat humid in winter,
by about half of the subjects who were stripped to the waist, even when
the dry-bulb temperature was 70 F or less. In summer, a relative humi-
dity of 30 per cent was pronounced as a little too dry by about a third of
the subjects wearing warm-weather clothing. So long as the temperature
was kept within proper limits, the majority of the subjects were unable to
detect sensations of humidity (i.e., too high, too low, or medium) when
the relative humidity was between 30 and 60 per cent. This is in accord
with studies by Howell23, Miura24 and others.
Dry air produces an excessive loss of moisture from the skin and respira-
tory tract. Owing to the cooling effect of evaporation, higher tempera-
tures are necessary, and this condition leads to discomfort and lassitude.
Moist air, on the other hand, interferes with the normal evaporation of
moisture from the skin, and again may cause a feeling of oppression and
lassitude, especially when the temperature is also high.
Just what the optimum range of humidity is, is a matter of conjecture.
There seems to exist a general opinion, supported by some experimental
and statistical data, that warm, dry air is less pleasant than air of a
moderate humidity, and that it dries up the mucous membranes in such
a way as to increase susceptibility to colds and other respiratory dis-
orders25- 26- 27.
For the premature infant, a high relative humidity of about 65 per cent
is demonstrably beneficial to health and growth28, and according to
Huntingdon29, this seems to be the case for adults also. All of these
studies indicate that the optimum humidity must always be considered
in combination with temperature.
Until more exact information is secured, it would be desirable to restrict
the comfort zones to the range of relative humidity employed in the
comfort zone experiments, namely, 30 to 70 per cent. Relative humidities
below 30 per cent may prove satisfactory from the standpoint of comfort,
so long as extremely low humidities are avoided. From the standpoint of
health, however, the consensus seems to favor a relative humidity between
^Humidity and Comfort, by W. H. Howell (The Science Press, April, 1931).
^Effect of Variation in Relative Humidity upon Skin Temperature and Sense of Comfort, by U. Miura
(American Journal of Hygiene, Vol. 13, 1931, p. 432).
^Reactions of the Nasal Cavity and Post-Nasal Space to Chilling of the Body Surface, by Mudd, Stuart,
et a! (Journal Experimental Medicine, 1921, Vol. 34, p. 11).
"Reactions of the Nasal Cavity and Post-Nasal Space to Chilling of the Body Surfaces, by A. Goldman,
et al and Concurrent Study of Bacteriology of Nose and Throat (Journal Infectious Diseases, 1921, Vol. 29,
p. 151).
^The Etiology of Acute Inflammations of the Noset Pharynx and Tonsils, by Mudd, Stuart, et al (Am.
Otol., RhinoL, and Laryngol., 1921).
^Application of Air Conditioning to Premature Nurseries in Hospitals, by C. P. Yaglou, Philip Drinker
and K. D. Blackfan (A.S.H.V.E. TRANSACTIONS, VoL 36, 1930).
^Weather and Health, by Ellsworth Huntington (Bulletin of the National Research Council No. 75.
The National Academy of Science, Washington, D. C., 1930).
45
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
40 and 60 per cent. In mild weather such comparatively high relative
humidities are entirely feasible, but in cold or sub-freezing weather they
are objectionable on account of condensation and frosting on the^ windows.
They may even cause serious damage to certain building materials of the
exposed walls by condensation and freezing of the moisture accumulating
inside these materials. Unless special precautions are taken to properly
insulate the affected surfaces, it will be necessary to reduce the degree of
artificial humidification in sub-freezing weather to less than 40 per cent,
according to the outdoor temperature. Information on the prevention of
condensation on building surfaces is given in Chapter 7. The principles
underlying humidity requirements and limitations are discussed more
fully elsewhere30.
The comfort chart (Fig. 3) applies to adults between 20 and 70 years
of age living in the northeastern parts of the United States. For pre-
maturely born infants, the optimum temperature varies from 100 F to
75 F, depending upon the stage of development. The optimum relative
humidity for these infants is placed at 65 per cent. ^ No data are yet
available on the optimum air conditions for full term infants and young
children up to school age. Satisfactory air conditions for these age
groups are assumed to vary from 75 F to 68 F with natural indoor humidi-
ties. For school children, the studies of the New York State Commission
on Ventilation place the optimum air conditions at 66 F to 68 F tempera-
ture with a moderate humidity (not specified) and a moderate but not
excessive amount of air movement (not specified)31.
Satisfactory comfort conditions are found to vary from 40 deg to 70 deg
ET, depending upon the rate of work and amount of clothing worn. The
effective temperatures giving maximum comfort for persons working have
been determined by the A.S.H.V.E. Research Laboratory32 for a rate of
work which is considered hard labor. For this degree of work, 50 per cent
were fairly comfortable for temperatures ranging from 46 to 64 deg ET,
while the greatest percentage found maximum comfort at 53 deg ET.
In hot industries, 80 deg ET is considered the upper limit compatible
with efficiency, and, whenever possible, this should be reduced to 70 deg
ET or less.
APPLICATION OF COMFORT CHART
The average winter comfort line (66 deg ET) applies to average
American men and women living inside the broad geographic belt across
the United States in which central heating of the convection type is
generally used during four to eight months of the year. It does not apply
to rooms heated by radiant energy, or to rooms with excessive glass area
or rooms with poorly insulated or cold walls, and it has not been advocated
officially for use in foreign countries where the climate, heating methods,
and general living conditions are materially different from those in the
United States, although several foreign workers have attempted to show
that it cannot be so applied. Even in the warm south and southwestern
*>Humidiiication for Residences, by A. P. Kratz (University of Illinois Engineering Experiment Station
Bulletin No. 230, July 28, 1931).
^Ventilation, Report of the New York State Commission on Ventilation, 1923.
»A.S.H.V.E. research paper entitled Heat and Moisture Losses from Men at Work and Application to
Air Conditioning' Problems, by F, C. Houghten, W. W. Teague, W. E. Miller and W. P. Yant (A.S.H'.V.E.
TRANSACTIONS, Vol. 37, 1931),
46
CHAPTER 2 — VENTILATION AND AIR CONDITIONING STANDARDS
climates, and in the very cold north-central climate of the United States,
the comfort chart would probably have to be modified according to
climate, living and working conditions, and the degree of acquired
adaptation.
In densely occupied spaces, such as classrooms, theaters and audi-
toriums, somewhat lower temperatures are necessary than those indicated
by the comfort line on account of counter-radiation between the bodies of
occupants22 in close proximity. In rooms in which the average wall
surface temperature is considerably below the air temperature, higher air
temperatures are necessary. The reverse holds true in radiant or panel
heating methods. (See Chapter 38.)
The sensation of comfort, in so far as the physical environment is con-
cerned, is not absolute but varies considerably among certain individuals.
Therefore, in applying the air conditions indicated by the comfort line,
it should not be expected that all the occupants of a room will feel per-
fectly comfortable. When the winter comfort line is applied in accordance
with the foregoing recommendations, the majority of the occupants will
be perfectly comfortable, but there will always be a few who would feel
a bit too cool and a few a bit too warm. These individual differences among
the minority should be counteracted by suitable clothing.
Air conditions lying outside the average comfort zone but within the
extreme comfort zone may be comfortable to certain persons. In other
words, it is possible for half of the occupants of a room to be comfortable
in air conditions outside the average comfort zone, but in the majority of
cases, if not in all, these conditions will be well within the extreme comfort
zone as determined experimentally.
Strictly speaking, the only authoritative comfort zone on which accur-
ate data are available, is that for 15 to 25 fpm air movement or tur-
bulance (often referred to as still air). In the past, the winter comfort
zone has often been superimposed on the thermometric chart or on effec-
tive temperature charts for various air velocities, on the assumption that
air conditions of equal warmth are approximately equally comfortable.
This may hold in hot industries where the workers are adapted to high
temperatures and strong air currents, but it does not apply to sedentary
conditions. To ascertain approximately whether a given industrial con-
dition is reasonably comfortable, it would be necessary first to compute
the effective temperature from the thermometric chart (Fig. 1) and then
to refer this effective temperature to the comfort chart (Fig. 3), or to
refer directly to a chart or table for the proper air velocity.
The summer comfort line (71 deg ET) is applicable to the same geo-
graphic area as the winter comfort line. It is further restricted to cases in
which the human body has reached thermal equilibrium with its environ-
ment. As a general rule this takes place after 1}^ to 3 hours' exposure.
When a person from outdoors enters a room cooled to 71 deg ET on a hot
day (95 F or over) an intense chill is likely to be experienced which is
unpleasant. However, after remaining in the room for about 2 hours,
this fundamental optimum condition will prove satisfactory to the average
person. The summer comfort zone, as well as the comfort line, makes
proper allowance for these adaptive changes in the body, and thus applies
to homes, offices, schools and other similar places where persons of
sedentary occupations speed from 3 to 8 or more hours daily.
47
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
In artificially cooled theaters, department stores, restaurants, and other
public buildings where the period of occupancy is short, the contrast
between outdoor and indoor air conditions becomes the deciding factor in
regard to the temperature and humidity to be maintained. The object of
cooling such places in the summer is not to reduce the temperature to the
optimum degree, but to maintain therein a temperature which is tem-
porarily comfortable to the patrons who thus avoid sensations of chill and
intense heat on entering and leaving the building. The relative humidity .
should be low enough (about 50 per cent or less) to give a sense of comfort
without chill and to induce a rate of evaporation which will keep clothing
and skin dry. For exposures less than 3 hours, desirable indoor conditions
in summer corresponding to various outdoor temperatures are given in
Table 2.
It should be kept in mind that southern people, with their more sluggish
heat production and lack of adaptability, will demand a comfort zone
several degrees higher than those given here for the more active people of
TABLE 2. DESIRABLE INDOOR AIR CONDITIONS IN SUMMER CORRESPONDING
TO OUTDOOR TEMPERATURES
Applicable to Exposures Less Than 3 Hours
OUTDOOR TEMPERATURE
(!>EG FAHB)
INDOOR Am CONDITIONS WITH DEW POINT
CONSTANT AT 57 F
DHT-BTJLB
DET-BTJLB
WET-BULB
EFFECTIVE TEMP
95
80.0
65.0
73
90
78.0
64.5
72
85
76.5
64.0
71
80
75.0
63.5
70
75
73.5
63.0
69
70
72.0
62.5
68
northern climates. Instead of the summer comfort line standing at
71 deg as here given, it was found to be much higher for foreigners in
Shanghai where climatic conditions are similar to those of our gulf
states. This difference in basic metabolic level of people forms a very
real problem for air conditioning engineers, which they must recognize in
their efforts to give proper conditions of comfort. Cooling of theaters,
resturants, and other public buildings in southern climates cannot be
based on northern standards without considerable modification.
A.S.H.V.E. VENTILATION STANDARDS33
It is the intent of the Committee in presenting this report to confine itself to a statement of those
requirements which, based on present day knowledge, will provide adequate ventilation for
spaces intended for human occupancy. The following standards shall apply to all spaces
occupied by human beings in all buildings for which ventilation regulations are to be established.
^Report of A.S.H.V.E. Committee on Ventilation Standards consisting of W. H. Driscoll, Chairman,
J. J. Aeberly, F. Paul Anderson, L. A. Harding, D. D. Kimball, J. R. McCoIl, C. L. Riley, W. A. Rowe,
Perry West and A. C. Willard, presented at the Serai-Annual Meeting of the Society, Milwaukee, Wis.,
June, 1932, and adopted by the Society in August, 1932.
48
CHAPTER 2 — VENTILATION AND AIR CONDITIONING STANDARDS
SECTION I— AIR TEMPERATURE AND HUMIDITY
The temperature and humidity of the air in such occupied spaces, and in which the only
source of contamination is the occupant, shall be maintained at all times during occu-
pancy at an Effective Temperature, as hereinafter stated.
The relative humidity shall be not less than 30 per cent, nor more than 60 per cent in
any case. The Effective Temperature shall range between 64 deg and 69 deg when
heating or humidification is required, and between 69 deg and 73 deg when cooling or
dehumidification is required.
These Effective Temperatures shall be maintained at a level of 36 in. above the floor.
(See Appendix, Tables A and B).
SECTION II— AIR QUALITY
The air in such occupied spaces shall at all times be free from toxic, unhealthful or
disagreeable gases and fumes and shall be relatively free from odors and dust.
In every space coming within the provisions of these requirements and in which the
quality of the air is below the standards prescribed by good medical and engineering
practices, due to toxic substances, bacteria, dust, excessive temperature, excessive
humidity, objectionable odors, or other similar causes, means for ventilating shall be
provided so that the quality of the air shall be raised to these standards.
SECTION III— AIR MOTION
The air in such occupied spaces shall at all times be in constant motion sufficient to
maintain a reasonable uniformity of temperature and humidity, but not such as to cause
objectionable drafts in any occupied portion of such spaces.
The air motion in such occupied spaces, and in which the only source of contamination
is the occupant, shall have a velocity of not more than 50 feet per minute, measured
at a height of 36 in. above the floor.
SECTION IV— AIR DISTRIBUTION
The air in all rooms and enclosed spaces shall, under the provisions of these reqr're-
ments, be distributed with reasonable uniformity, and the variation in the carbon dioxide
content of the air shall be taken as a measure of such distribution.
The air in a space ventilated in accordance with these requirements, and in which the
only source of contamination is the occupant, shall be distributed and circulated so that
the variation in the concentration of carbon dioxide, when measured at a height of
36 in. above the floor, shall not exceed one part in 10,000.
SECTION V— AIR QUANTITY
The quantity of air used to ventilate the given space during occupancy shall always
be sufficient to maintain the standards of air temperature, air quality, air motion and air
distribution as herein required. Not less than 10 cubic feet per minute per occupant of
the total air circulated to meet these requirements shall be taken from an outdoor source.
APPENDIX
Definitions
For the purposes of these standards the terms used shall be defined as follows: —
Ventilation : The process of supplying or removing air by natural or mechanical means, to or from any
space. Such air may or may not have been conditioned. (See Air Conditioning).
Air Conditioning: The simultaneous control of all or at least the first three of those factors affecting
both the physical and chemical conditions of the atmosphere within any structure. These factors include
temperature, humidity, motion, distribution, dust, bacteria, odors, toxic gases, and ionization, most of
which affect in greater or lesser degree human health or comfort.
Dry-Bulb Temperature: The temperature of the air which is indicated by any type of thermometer
which is not affected by the water vapor content or relative humidity of the air.
Dust: Solid material in a finely divided state, the particles of which are large and heavy enough to fall
with increasing velocity, due to gravity in still air. For instance, particles of fine sand or grit, such as are
blown on a windy day, the average diameter of which is approximately 0.01 centimeter, may be called dust.
Effective Temperature: An arbitrary index of the degree of warmth or cold felt by the human body
in response to temperature, humidity, and movement of the air. Effective temperature is a composite
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Index which combines the readings of temperature, humidity, and air motion into a single value. The
numerical value of the effective temperature scale has been fixed by the temperature of saturated air which
induces an identical sensation of warmth.
Humidity: The water vapor (either saturated or superheated steam) occupying any space, which may
or may not contain other vapors and gases at the same time.
Relative Humidity: A ratio, although usually expressed in per cent, used to indicate the degree of
saturation existing in any given space resulting from the water vapor present in that space. The presence
of air or other gases in the same space at the same time has nothing to do with the relative humidity of
the space, which depends merely on the temperature and partial pressure of the vapor.
Spaces in Which the Only Source of Contamination Is the Occupant: Spaces in which the
atmospheric contamination results entirely from the respiratory processes of the occupant, including heat,
moisture, and odors given off by the body. No manufacturing or industrial processes or other sources of
atmospheric contamination, including heat and moisture, than people are considered under this title.
TABLE A. EFFECTIVE TEMPERATURES RANGING FROM 64 DEC TO 69 DEC FOR VARIOUS DRY- BULB TEM-
PERATURES AND RELATIVE HUMIDITIES FOR STILL AIR FOR PERSONS
NORMALLY CLOTHED AND SLIGHTLY
(For use when heating or humidification is required)
RELATIVE HUMIDITIES (PER CENT)
DRY- BULB
TEMPERATURES
(DEC FAHR)
30 ^ 35
40 45
50
55
60
EFFECTIVE TEMPERATURES (DEGREES)
67
64.0
64.3
68
64.0
64.2
64.5
64.8
65.1
69
64.1
64.4
64.8
65.1
65.4
65.7
66.0
70
64.8
65.1
65.4
65.8
66.2
66.5
66.8
71
65.5
65.8
66.2
66.6
67.0
67.3
67.7
72
66.2
66.5
66.9
67.3
67.7
68.1
68.5
73
67.0
67.3
67.7
68.1
68.5
68.9
74
67.7
68.0
68.4
68.8
75
68.4
68.7
76
69.0
aSee Fig. 3.
TABLE B. EFFECTIVE TEMPERATURES RANGING FROM 69 DEC TO 73 DEC FOR VARIOUS DRY-BULB TEM-
PERATURES AND RELATIVE HUMIDITIES FOR STILL AIR FOR PERSONS
NORMALLY CLOTHED AND SLIGHTLY AcTivEa-b
(For use when cooling or dehumidification is required)
RELATIVE HUMIDITIES (PER CENT)
DRY-BULB
TEMPERATURES
(DEG FAHR)
30
35
40
45
50
55
60
EFFECTIVE TEMPERATURES (DEGREES)
73
69.3
74
69.3
69.7
70.1
75
69.1
69.5
70.0
71.5
71.0
76
69.0
69.4
69.9
70.5
70.8
71.3
71.8
77
69.7
70.2
70.7
71.2
71.6
72.1
72.6
78
70.4
70.9
71.4
71.9
72.4
73.0
79
71.1
71.6
72.2
72.6
80
71.8
72.4
72.9
81
72.5
•See Fig, 3.
bThis table applies primarily to cases in which the human body has reached equilibrium with the sur-
rounding air. A higher plane of summer effective temperatures is required in places of public assembly
where the period of occupancy is short, than is required for offices and industrial plants where the period of
occupaacy isjrf longer duration. When the period of occupancy is two hours or less, the dry-bulb tempera-
ture shall be 72 F plus one-third of the difference between the outside dry-bulb temperature and 70 F, and
the relative humidity shall not exceed 60 per cent. (See also Table 2.)
50
CHAPTER 2 — VENTILATION AND AIR CONDITIONING STANDARDS
FACTORS INFLUENCING APPLICATIONS
The conditions and limitations outlined under the heading Application
of Comfort Chart should be noted in applying the temperatures and
relative humidities specified in Tables A and B of the preceding
A.S.H.V.E. Ventilation Standards.
Air Quality
In occupied spaces in which the vitiation is entirely of human origin,
the chemical composition of the air, the dust, and bacteria content may be
dismissed from consideration so that the problem consists in maintaining
a suitable temperature with a moderate humidity, and in keeping the
atmosphere free from objectionable odors. Such unpleasant odors,
human or otherwise, can be easily detected by persons entering the room
from clean, odorless air. A further discussion of air quality will be found
in Chapters 15 and 16.
Air Motion
As a result of studies by Baetjer34 and work carried on by the A.S.H.V.E.
Research Laboratory, it is now recognized that the importance of air
motion in air conditioning ranks only second to temperature. Air in an
occupied space having all the other essential qualities but lacking in air
motion feels stagnant, stuffy, and depressing, because the vitiated air
next to the body is not replaced by the surrounding air possessing the
satisfactory qualities. Hence, air motion is absolutely essential that an
occupant may realize the other desired qualities of the atmosphere.
Possible limits in variation in air motion may range from 5 fpm to 50 fpm,
as measured by the Kata thermometer. (See Chapter 40.) However,
satisfactory results are more likely to be insured by air velocities ranging
from 15 to 30 fpm. The limit of 5 fpm may be taken as the minimum
during the heating season, and 50 fpm as the maximum for the cooling
season.
Air Distribution
Variation in concentration of carbon dioxide in different parts of an
occupied room has been used as a measure of satisfactory distribution of
the outside or conditioned air supply. For satisfactory air distribution,
the carbon dioxide concentration at the 36-in. level should not vary by
more than one part in 10,000 parts of air. Recent work2 by the A.S.H.V.E.
Research Laboratory demonstrates that variations in dry-bulb tempera-
ture, wet-bulb temperature, or moisture content of the air are equally
good indices of air distribution. This work also indicates that the
presence of satisfactory air motion within the room (15 to 30 fpm as
measured by the Kata thermometer) insures satisfactory distribution.
Because of the laborious and exacting technique involved in making
carbon dioxide determinations, it is recommended that satisfactory
distribution can be amply insured by the presence of such air velocities in
all parts of the room together with dry-bulb temperature variations of not
to exceed 3 deg at the 36-in. level.
^Threshold Air Currents In Ventilation (American Journal of Hygiene, Vol. IVr No. 8, p. 650, 1924).
51
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Air Quantity
The quantity of air to be circulated through an occupied space, whether
by natural or mechanical means, or whether the air is conditioned or not,
must in all cases be sufficient to maintain the required standards of air
temperature, quality, motion and distribution. The factors which deter-
mine air quantity include the type and nature of the building, locality,
climate, height of rooms, floor area, window area, extent of occupancy,
and last but not least, the method of distribution.
The quantity of air supplied to a room by an air conditioning or venti-
lating system serves two purposes: First, the supply of sufficient outside
air for the needs of the occupants; and second, the setting up of circulation
or air motion within the room. Until recently it was considered that
30 cfm were necessary in any occupied space, particularly in a classroom,
It has since been demonstrated that 10 cfm of outside air per person is
frequently sufficient to remove body heat, insure against body odors,
and provide the chemical needs of respiration. However, it is found
that a greater volume should be circulated in the average room in
order to provide the required air motion. It is now customary to supply
the minimum amount of outside or conditioned air required for removing
heat and odors, and to recirculate the additional volume.
In offices and small rooms where the occupants smoke, from 6 to 7 cfm
of outside air per occupant will be necessary to eliminate the nuisance
effects of the smoke ; this quantity of air, however, may be a part of that
necessary. for other ventilation requirements. Restaurants which permit
smoking, because of the exposed food and the necessity that restaurant
air seem very clean, need from 10 to 12 cfm of outside air per occupant to
care for the smoke condition. This air, likewise, need not be in addition
to that required for other ventilation purposes.
Temperature Rise
The total quantity of air introduced is governed largely by the needs
for controlling temperature and humidity when either heating or cooling
is required. As a rule, the introduction and distribution of warm air into
an occupied space does not present as many difficulties as does the intro-
duction of cold air. The former is determined from the amount of heat to
be given up to the space, and the latter is determined from the amount of
heat to be removed from the space, using a temperature rise that will
produce uniform distribution without the production of disagreeable
drafts.
Fig. 4 shows the changes in carbon dioxide concentration and moisture
content resulting from occupation, in the atmosphere of a room supplied
with various volumes of outside air. Data are given for an adult, 5 ft
8 in. in height weighing 150 pounds and having a body surface area of
19.5 sq ft, and for a child, 12 years of age, 4 ft 7 in. in height, weighing
76.6 pounds and having a body surface area of 12.6 sq ft. It is a recognized
fact that the dissipation of heat and moisture to the atmosphere, the
addition of carbon dioxide, and all metabolic changes take place in pro-
portion to the surface area of the individual. Hence, data for persons of
other sizes may be obtained by interpolating among the curves given.
The rate of sensible heat production is given in Fig. 7. Fig. 4 also gives
52
CHAPTER 2 — VENTILATION AND AIR CONDITIONING STANDARDS
the temperature of the incoming air necessary to maintain a room tem-
perature of either 70 or 80 F as indicated, assuming that there is no heat
gain or loss to the room by transmission through the walls, solar radiation
or other sources.
ADULTS IN 63 F TO 86 F AIR
CHILDREN IN 63 F TO
ADULTS IN 8OF AIR
CHILDREN IN 8O F AIR
ADULTS IN 70 F AIR
CHILDREN IN 70 F AIR
CHILDREN IN 80 F AIR-
ULTS IN 80 F AIR
CHILDREN IN 70 F AIR
ADULTS IN 70 F AIR
12 16 20
RATE OF AIR SUPPLY
CUBIC FEET PER MINUTE PER OCCUPANT
24
FIG. 4. RELATION AMONG RATE OF AIR CHANGE PER OCCUPANT, CARBON DIOXIDE
CONCENTRATION AND MOISTURE CONTENT OF ENCLOSURE, AND DRY-BULB
TEMPERATURE OF^ INCOMING AIR
Two of the most important factors on which the temperature rise
depends are (1) the method of distribution and (2) the most economical
temperature rise for the conditions involved. Some systems of distri-
53
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
bution produce drafts with but a few degrees temperature rise, while
other systems operate successfully with a temperature rise as high as
35 deg. The total air quantity introduced in any particular case is
inversely proportional to the temperature rise, and depends largely upon
the judgment and ingenuity of the engineer in designing the most suitable
system for the particular conditions. Small quantities of air reduce the
size of equipment, ducts, space, and initial cost, but require lower air
temperatures. In any specific case, the cost of refrigeration must be
balanced against the extra cost in increased size of equipment and
running expense.
Outside Air. In order to provide uniform temperature conditions, it
is necessary to maintain a pressure of about 0.1 in. of water in the room or
space to be ventilated or conditioned. This usually requires the intro-
duction of a certain amount of outside air which depends on the particular
conditions involved, and may vary over a considerable range.
In rooms in which the only source of contamination is the occupant the
minimum quantity of outside or new air to be circulated appears to be
that necessary to remove objectionable body odors. The concentration of
body odors in turn depends largely upon the temperature of the air ; the
higher the temperature, the greater the amount of perspiration (sensible
or insensible) given off from the skin, and the greater the concentration
of odors.
NATURAL AND MECHANICAL VENTILATION
Under favorable conditions natural ventilation methods properly
combined with means for heating may be sufficient to provide for the
foregoing standards. As a rule, in instances in which the only source of
contamination is the occupant, the requirements may be fulfilled when
the following conditions prevail:
1. At least 50 sq ft of floor area for each occupant.
2. At least 500 cu ft of air space per occupant.
3. Effective openings in windows and skylights equal to at least 5 per cent of the
floor area.
Whenever natural means are not sufficient to maintain the standards,
resort must be made to whatever modifications or mechanical apparatus
are necessary to secure such standards.
In large offices, large school rooms, and in public and industrial build-
ings, natural ventilation is uncertain and makes heating difficult. The
chief disadvantage of natural methods is the lack of control : they depend
largely on weather and upon the velocity and direction of the wind.
Rooms on the windward side of a building may be difficult to heat and
ventilate on account of drafts, while rooms on the leeward side may not
receive an adequate amount of air from out of doors. The partial vacuum
produced on the leeward side under the action of the wind may even
reverse the flow of air so that the leeward half of the building has to take
the drift of the air from the rooms of the windward half. Under such
conditions no outdoor air would enter through a leeward window opening,
but room air would pass out.
In warm weather natural methods of ventilation afford little or no
54
CHAPTER 2 — VENTILATION AND AIR CONDITIONING STANDARDS
control of indoor temperature and humidity. Outdoor smoke, dust and
noise constitute other limitations of natural methods.
REC1RCULATION
The saving in operating costs due to recirculation of the air, while very
considerable, must not be obtained at the expense of air quality. The
percentage of recirculated air may be varied to suit the seasonal changes
so as to conserve heat in winter and refrigeration in summer, but at no
time during occupancy should there be taken from out of doors less than
10 cfm for each ^ occupant. ^As a general rule, recirculation impairs the
quality of the air by excessive humidity (if not conditioned), excessive
odors, or both, and it tends to deprive the air of its ionic content, but
77/ff
FIG. 5. INFLUENCE OF ROOM OCCUPANCY ON IONIC CONTENT^
(Cubical Contents of Room, 10,000 Cu Ft; Number of Occupants, 34)
the influence of this factor on comfort and health is at present a matter
of speculation.
Toilets, kitchens, and similar rooms, in buildings using recirculation,
should be separately mechanically ventilated by exhausting the air from
them in order to prevent objectipnable odors from diffusing into other
parts of the building.
ULTRA-VIOLET RADIATION AND IONIZATION
In spite of the rapid advances made in the field of air conditioning
during the past few years, the secret of reproducing, in indoor spaces,
atmospheres of as stimulating qualities as those existing outdoors in the
country, under ideal weather conditions, has not as yet been found. In
fact, extensive studies have failed to elucidate the cause of the stimulating
quality of outdoor country air, qualities which are lost when such air is
brought indoors and particularly when it is handled by mechanical
55
AMERICAS SOCIETY of HEATIKG and VENTILATING ENGINEERS GUIDE, 1935
TABLE 3. RELATION BETWEEN METABOLIC RATE AND ACTIVITY*
A.C7IVITT
METABOLIC RATE Brtr
PEB HOTTR FOR AVERAGE
MAN (19-5 SQ FT SUB-
FACE AREA)
ACTHORITT
Seated at rest
384
Research Laboratory, American Society of
Standing at rest
431
Heating and Ventilating Engineers.
Research Laboratory, American Society of
Walking 2 mph
761
Heating and Ventilating Engineers.
Average values from Douglas, Haidane,
Walking 3 rnph
1049
Henderson and Schneider; and Henderson
and Haggard.
Douglas, Haldane, Henderson and Schneider
Walking 4 mph
1388
Average values from Douglas, Haldane,
\Valking 5 mph
2530
Henderson and Schneider; and Henderson
and Haggard.
Douglas, Haldane, Henderson and Schneider
Slow run .
2285
Henderson and Haggard
Very severe exercise-.. .
Maximum exertion
Tailor
2555
3333 to 4762 -h
482
Benedict and Carpenter
Henderson and Haggard
Becker and Hamalainen
Bookbinder
626
Becker and Hamalainen
Shoemaker . ..
661
Becker and Hamalainen
Carpenter
762 to 963
Becker and Hamalainen
Metal worker
862
Becker and Hamalainen
Painter (of furniture)..
Stonemason
876
1488
Becker and Hamalainen
Becker and Hamalainen
Man sawing wood
1797
Becker and Hamalainen
means. It is true that many suggestions have been advanced to account
for the stimulating quality of outdoor air, such as ultra.- violet light _and
ionization. At the present time neither of these suggestions has received
any degree of scientific confirmation.
It is generally recognized that total outdoor solar radiation has marked
curative value in certain diseases and is also a powerful germicidal agent.
A critical review of the literature, however, does not substantiate the
theory that ultra-violet radiation is of importance in air conditioning,
since "the use of ultra-violet sources fails to produce indoors, the pre-
viously mentioned stimulating qualities found in outdoor air.
Experiments35 show that in occupied rooms there is a marked decrease
in both positive and negative small ions. As shown in Fig. 5, soon after
the occupants assembled the ionic content fell abruptly to a very low level
which was maintained until the occupants left the room. Both positive
and negative ions began to rise again as soon as the occupants departed.
The effects of the decrease in the ionic content of indoor air on comfort
and health have not yet been subjected to sufficient scientific investiga-
tion. It would appear, however, from the evidence at hand, that comfort
is not associated with a high ion content — but this must be considered, at
least for the time being, as still a subject for further study.
»A.S.H.V.E. research paper entitled Changes in Ionic Content in Occupied Rooms, Ventilated by
Natural and Mechanical Methods, by C. P. Yaglou, L. C. Benjamin and S. P. Choate (A.S.H.V.E. TRANS-
ACTIONS, Vol. 37, 1931). Physiologic Changes During Exposure to Ionized Air, by C. P. Yaglou, A. D.
Brandt and L. C. Benjamin (A.S.H.V.E. Journal Section, Heating, Piping and Air Conditioning, August,
1933). Diurnal and Seasonal Variations in the Small Ion Content of Outdoor and Indoor Air, by C. P.
Yaglou and L. C. Benjamin, (A.S.H.V.E. Journal Section, Heating, Piping and Air Conditioning. January.
1934). The Nature of Ions in Air and their Possible Physiological Effects, L. B. Loeb (A.S.H.V.E. Journal
Section, Heating, Piping and Air Conditioning, October, 1934).
56
CHAPTER 2 — VENTILATION AND AIR CONDITIONING STANDARDS
HEAT AND MOISTURE LOSSES
In order to solve air conditioning problems involving the human body
it is necessary to know the rate at which sensible and latent heat are given
up by the body under various conditions of temperatue and activity.
Research at the A.S.H.V.E. Laboratory M» 35 has resulted in the data given
in Figs, 7, 8, and 9. Table 3 gives the metabolic rates for various degrees
of activity.
The experimental data from which the curves were drawn show that
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EFFECTIVE TEMPERATURE "FAHR.
FIG. 6. RELATION BETWEEN TOTAL HEAT Loss FROM
THE HUMAN BODY AND EFFECTIVE TEMPERATURE
FOR STILL AiRa
aCurve A — Men working 66,160 ft-lb per hour. Curve B —
Men working 33,075 ft-lb per hour. Curve C — Men working
16,538 ft-lb per hour. Curve D — Men seated at rest. Curves A and
C drawn from data at an effective temperature of 70 deg only and
extrapolating the relation between curves B and D, which were
drawn from data at many temperatures.
total heat loss does not vary appreciably within the comfort zone (see
Fig. 6). Above or below this range the variation is approximately a
function of effective temperature. Sensible and latent heat losses (Figs.
7 and ^9) on the other hand, vary greatly within the comfort zone, the
variation following closely the dry-bulb temperature.
Although total heat loss and sensible and latent heat losses are not
exact functions of effective and dry-bulb temperature, respectively, for all
t? Jf1^6"11?1 Exchanges Between the Bodies of Men Working and the Atmospheric Environment, by
N 2 M hCIlVn W" Teagne* W" E' Maier' and w- p- Yant (American Journal of Hygiene, Vol. XIII,
57
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
conditions of humidity and air motion, they are plotted as such in the
curves. This is accomplished by approximations which are sufficiently
accurate for application to practical problems. Comparison of Figs.
7 and 8 shows how the cooling load may vary between sensible and latent
heat elimination for different atmospheric conditions and activities of
occupants.
An atmospheric condition resulting in sensible perspiration is to be
laoo
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£ 700
6OO
. SCO
s
£400
rr 300
d
i200
H 100
30°
4<f 53s 60^ 7tf 80T 90°
DRY BULB TEMPERATURE °FAHR.
100°
FIG. 7. RELATION BETWEEN SENSIBLE HEAT Loss
FROM THE HUMAN BODY AND DRY-BULB TEMPERATURE
FOR STILL AiRa
aCurve A — Men working 66,150 ft-lb per hour. Curve B —
Men working 33,075 ft-lb per hour. Curve C— -Men working
16,538 ft-lb per hour. Curve D — Men seated at rest. Curves A and
C drawn from data at a dry-bulb temperature of 81.3 F only and
extrapolating the relation between curves B and D which were
drawn from data at many temperatures.
avoided for obvious reasons. Tables 4 and 5 give the approximate effec-
tive temperatures at which perspiration is noticeable in different degrees
for 95 per cent and 20 per cent relative humidity.
In theaters, auditoriums, department stores and other crowded en-
closures, the amount of heat and moisture given off by the people is so
large that normal changes in outside temperature and humidity have
relatively little effect on indoor air conditions. The principal object of air
conditioning in such places is to remove excessive heat and moisture by
supplying a sufficient quantity of properly conditioned air. The indoor
air conditions, however, must be varied according to the outside tem-
perature, as has been pointed out.
58
CHAPTER 2 — VENTILATION AND Am CONDITIONING STANDARDS
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DRY BULB TEMPERATURE
FIG. 8. LATENT HEAT AND MOISTURE Loss FROM THE HUMAN BODY BY EVAPORATION,
IN RELATION TO DRY-BULB TEMPERATURE FOR STILL AIR CONDITIONS^-
aCmrve A — Men working 66,150 ft-lb per hour. Curve B — Men working 33,075 ft-Ib per hour.' Carve
C— Men working 16,538 ft-Ib per hour. Curve D — Men seated at rest. Curves A and C drawn from data
at a dry-bulb temperature of 81. 3 F only and extrapolating the relation between Curves Band D which
were drawn from data at many temperatures.
x>
°
95°
FIG. 9. HEAT Loss FROM THE HUMAN BODY BY EVAPORATION, RADIATION AND CON-
VECTION IN RELATION TO DRY-BULB TEMPERATURE FOR STILL AIR
aCurve A — Men working 66,150 ft4f> per hoar. Curve B— Men working 33,075 ft-Ib per Lour. Curve
C— Men working 16,538 ft-lb Vex hour. Curve D — Men seated at rest. Curves A and C drawn from data
at a dry-bulb temperature of 81.3 F only and extrapolating the relation between Curves B and D which were
drawn from data at many temperatures.
59
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Although heat and moisture from the human body constitute the major
portion of the cooling load, in most cases where air conditioning is pro-
vided for comfort and health other factors must also be considered. These
include heat from lights, machinery, and processes, as well as the trans-
mission and infiltration of heat through the building structure. The
computations for these factors may be made in accordance with data
given in Chapters 5 and 7.
TABLE 4.
CONDITION OF SENSIBLE PERSPIRATION FOR PERSONS SEATED AT REST
UNDER VARIOUS ATMOSPHERIC CONDITIONS*
DEGBEE OF PERSPIRATION*
95 Per Cent Relative
Humidity
20 Per Cent Relative
Humidity
E. T.
D.B.
W. B.
E. T.
D.B
W. B.
Forehead clammy - —
73.0
73.0
79.0
80.0
84.5
88.0
88.5
73.6
73.6
79.7
80.8
85.4
89.0
89.5
72.4
72.4
78.4
79.4
84.0
87.6
88.1
75.0
75.0
81.0
87.0
86.5
94.0
90.0
87.0
87.0
97.5
109.4
108.5
125.2
116.0
60.7
60.7
67.5
75.2
74.6
85.4
79.5
Body clammy
Body damp . .-- .. —
Beads on forehead
Body wet
Perspiration on forehead runs and drips
Perspiration runs down body
ATMOSPHERIC CONDITION
aForty per cent of subjects registered degree of perspiration equal to or greater than indicated.
TABLE 5.
CONDITION OF SENSIBLE PERSPIRATION FOR PERSONS AT WORK
UNDER VARIOUS ATMOSPHERIC CONDITIONS^
DEGREE OP PERSPIRATION*
95 Per Cent Relative
Humidity
20 Per Cent Relative
E.T.
D.B.
W.B.
E.Y.
D.B.
W.B.
Forehead clammy
Body clammy _.
59.0
50.0
60.0
68.0
69.0
78.5
79.0
59.4
50.2
60.3
68.5
69.6
79.3
79.8
58.3
49.3
59.3
67.5
68.5
78.0
78.5
69.5
57.0
62.5
76.0
71.0
82.0
81.0
80.5
61.6
69.6
91.0
82.8
100.5
99.8
56.5
44.2
49.5
63.4
53.0
70.2
69.0
Body damp .
Beads on forehead, „
Body wet .
Perspiration on forehead runs and drips
Perspiration runs down body
ATMOSPHERIC CONDITION
•Forty per cent of subjects registered degree of perspiration equal to or greater than indicated.
In many cases, allowance must also be made for sun effect and for heat
capacity of the building structure in accordance with studies by the
A.S.H.V.E. Research Laboratory37. Another item to be considered is the
radiant heat received by the body from high temperature wall and celling
surfaces.
^Heat Transmission as Influenced by Heat Capacity and Solar Radiation, by F. C. Houghten, J. L.>
Blackshaw, E. M. Pugh, and Paul McDermott (A.S.H.V.E. TRANSACTIONS, Vol. 38, 1932).
60
CHAPTER 2 — VENTILATION AND AIR CONDITIONING STANDARDS
PROBLEMS IN PRACTICE
1 • What is the purpose and method of conditioning the air of occupied rooms?
Chiefly comfort, and the method is to control the temperature, humidity, and air distri-
bution, and to prevent the accumulation of excessive body odors in the air. Other
factors have yet to be studied.
2 • What are the most comfortahle air conditions?
Comfort standards are not absolute, but they are greatly affected by the physical con-
dition of the individual, and the climate, season, age, sex, clothing, and physical activity.
For the northeastern climate of the United States, the conditions which meet the require-
ments of the majority of people consist of temperatures between 68 and 72 F in winter
and between 70 and 85 F in summer, the latter depending largely upon the prevailing
outdoor temperature. The most desirable relative humidity range seems to be between
30 and 60 per cent.
3 • Are the optimum conditions for comfort identical with those for health?
There are no absolute criteria of the prolonged effects of various air conditions on health.
For the present it can be only inferred that bodily discomfort may be an indication of
conditions that may produce poor health.
4 • Given dry -bulb and wet-bulb temperatures of 76 F and 62 F, respectively,
and an air velocity of 100 fpm, determine: (1) effective temperature of the con-
dition; (2) effective temperature with still air; (3) cooling produced by the move-
ment of the air; (4) velocity necessary to reduce the condition to 66 deg effective
tempera tur e .
(lj In Fig. 1 draw line AB through given dry- and wet-bulb temperatures. Its
intersection with the 100-ft velocity curve gives 69 deg for the effective temperature of
the condition . (2) Follow line A B to the right to its intersection with the 20-f pm velocity
line, and read 70.4 deg for the effective temperature for this velocity or so-called still air.
(3) The cooling produced by the movement of the air is 70.4 — 69 = 1.4 deg effective
temperature. (4) Follow line AB to the left until it crosses the 66 deg effective tempera-
ture line and interpolate velocity value of 340 fpm to which the movement of the air
must be increased.
5 • Given dry-bulb and wet-bulb temperatures of 75 and 68 F, respectively,
first, what is the effective temperature? Second, is this condition warmer or
cooler than 80 F dry-bulb and 60 F wet-bulb?
The first condition is given by the intersection of the 75 F dry-bulb line and the 68 F wet-
bulb line (Fig. 3). The effective temperature of 72.1 deg is given by the numerical value
of the effective temperature line passing through this point and indicated by the scale
along the saturation curve. The second condition is given by the intersection of 80 F
dry-bulb and 60 F wet-bulb and is 71.8 deg ET. It is therefore 0.3 deg ET cooler than
the first condition.
6 • Given 76 F dry-bulb and 61 F wet-bulb, how many degrees difference
are there between this condition and the winter comfort line or 66 deg ET?
The effective temperature for this condition is given by the intersection of the 76-F dry-
bulb and 61-F wet-bulb lines and is 70 deg ET, which is 4 deg ET warmer than the
comfort line.
7 • Assume that the design of an air conditioning system for a theater is to be
based on an outdoor dry-bulb temperature of 95 F and a wet-bulb temperature
of 78 F with an indoor relative humidity of 50 per cent. According to Table 2,
the dry-bulb temperature in the auditorium should be 80 F. Estimate the
sensible and latent heat given up per person.
The sensible heat given up per person per hour under this condition may be obtained
from Fig. 7. With an abscissa value of 80 F, Curve D for men seated at rest gives a value
on the ordinate scale of 220 Btu per person per hour as the sensible heat loss. The latent
heat given up by a person seated at rest per hour may be obtained from Fig. 8. With an
61
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
abscissa value of SO FT Curve D indicates a latent heat loss of 175 Btu per hour left hand
scale) or a moisture loss of 1190 grains per hour (right hand scale).
8 • How much sensible heat, how much latent heat and how much water
vapor wUl be added per hour to the atmosphere of an auditorium by an audience
of 1000 adults, when the dry- and wet-bulb temperatures are 75 F and 63.5 F,
respectively?
From Curve D, Fig, 7, find the sensible heat loss per person for a dry-bulb temperature
of 75 F and still air to be 265 Btu per hour. From Fig. 8 find the latent heat loss per
person for a dry-bulb temperature of 75 F to be 134 Btu per hour and the moisture
added to be 905 grains per hour. Sensible heat = 1000 X 265 = 265,000 Btu. Latent
heat = 1000 X 134 = 134,000 Btu. Water vapor added per hour to the air in the
auditorium = 1000 X 905 = 905,000 grains or 129 Ib.
The sensible and latent heat added to the air may also be found as follows: The effective
temperature for dry- and wet-bulb temperatures of 75 F and 63.5 F, respectively, is
70.3 deg. From Curve D, Fig. 6, find 403 Btu as the total heat added to the air by a
person for an effective temperature of 70.3 deg. From Fig. 9 find the percentage of
sensible and latent heat at a dry-bulb temperature of 75 F to be 66.5 per cent and 33.5
per cent. The sensible heat added to the air in the auditorium is 1000 X 0.665 X 403 =
267,995 Btu per hour. The latent heat added is 1000 X 0.335 X 403 = 135,005 Btu
per hour.
9 • If the dry- and wet-bulb temperatures of the auditorium were 85 F and
63 F, respectively, how much heat and moisture would be dissipated to the
atmosphere?
From Figs. 7 and 8, respectively, the sensible and latent heat losses per person for a dry-
bulb temperature of 85 F are found to be 164 and 225 Btu per hour. The water vapor
added to the atmosphere is 1520 grains per hour. The audience will then add 164,000
Btu sensible heat, 225,000 Btu latent heat and 1,520,000 grains or 217 Ib of water vapor
to the air in the auditorium per hour.
10 • Neglecting the gain or loss of heat to an auditorium by transmission or
infiltration through the walls, windows and doors, how many cubic feet of
outside air, with dry- and wet-bulb temperatures of 65 F and 59 F, respectively,
(63.1 deg ET) must be supplied per hour to an auditorium containing 1000
people in order that the inside shall not exceed 75 F (dry-bulb) and 65 F (wet-
bulb), respectively?
Figs. 7 and 8 give 265 Btu sensible heat and 905 grains of moisture as the additions per
person with a dry-bulb temperature of 75 F in the auditorium. Therefore, 265,000 Btu
of sensible heat and 905,000 grains of moisture will-be added to the air in the auditorium
per hour.
Taking 0.24 as the specific heat of airf 2.4 Btu per pound of air will be required to raise
oopr QAQ
the dry~bulb temperature from 65 to 75 F and ' = 110,400 Ib of air or 110,400 X
^.4
1 47Q 000
13.4 = 1,479,000 cfh of air will be required. This is equivalent to ^A J/gn = 24-7 cfm
ILKJU X oU
per person.
The moisture content of the inside air as taken from a psychrometric chart is 76 grains
per pound of dry air and that of the outside condition is 65 grains. The increase in
905 000
moisture content will therefore be 11 grains per pound of dry air. Hence — ~~^- — =
82,300 Ib of air at the specified condition will be required. This is equivalent to 82,300
i 1 02 OOO
X 13.4 = 1,103,000 cfh of air or /QQQ ^ 6Q « 18.4 cfm of air per person.
The higher volume of 24.7 cfm per person will be required to keep the dry-bulb tem-
perature from rising above the 75 F specified. The wet-bulb temperature will therefore
not rise to the maximum of 65 F.
11 • Assume that a man performs work at a rate equivalent to 50,000 ft-lb per
hour, in an atmosphere having a dry-bulb temperature of 70 F. Estimate the
sensible and latent heat given off per hour.
62
CHAPTER 2 — VENTILATION AND AIR CONDITIONING STANDARDS
Since the net mechanical efficiency of the human body is about 20 per cent, the increase
oO 000
in metabolism due to work, over the resting metabolism, will be -^,--Lrn-oh = ^20 Btu
/ / o X U.^U
per hour. Assuming a resting metabolism of 400 Btu per hour ^see Fig. 6), the total
metabolism during work will be 400 -f- 320 = 720 Btu per hour, and the total heat loss
720 — ^ _', - = 656 Btu per hour, approximately. In Fig. 9, follow a vertical line from
/ /o
a dry-bulb temperature of 70 F to a point midway between Curves /I and B. The sensible
heat loss is about 46 per cent of the total loss, or 0.46 X 656 = 302 Btu per hour, and the
latent heat is 54 per cent of the total or 0.54 X 656 = 354 Btu per hour.
12 • The characteristics of air supplied to ventilate a room are:
Carbon dioxide concentration , . . . A parts per 10,000
Wet-bulb temperature . - 45.2 F
Dry-bulb temperature , . . . „ 55.0 F
Moisture content 29.0 grains per pound of dry air
a. What will be the dry -bulb temperature of the air in the room if it is occupied
by five adults, if the air change, including both ventilation and infiltration, is
50 cu ft per minute, and assuming that there is no heat gain or loss to the room
from any source other than from the occupants?
b. What will be the carbon dioxide concentration of the air in the room under
these conditions?
c. What will be the moisture content of the ah* in the room under these con-
ditions?
d. What will be the wet-bulb temperature and the relative humidity of the air
in the room under these conditions?
e. WTiat would the temperature of the incoming air have to be to give a room a
dry-bulb temperature of 70 F?
a. The air change is 10 cu ft per minute per occupant. From the bottom chart of Fig. 4
at the intersection of an incoming air dry-bulb temperature of 55.0 F and a rate of air
supply of 10 cu ft per minute per occupant, find by interpolation between the 70 F and
80 F adult curves the dry-bulb temperature of the air in the room to be 78.0 F.
b. From the top chart of Fig. 4 find the increase in CO2 concentration to be 10 parts of
CC>2 per 10,000 parts of air. Therefore, the air in the occupied room will contain 14
parts of CO2 per 10,000.
c. From the center chart in Fig, 4 find by interpolation between the 70 F and 80 F adult
curves the increase in moisture content to be 23 grains per pound of dry air for adults in
78 F air. This gives a resultant moisture content of the air in the room of 52 grains per
pound of dry air.
d. From the psychrometric chart, Fig. 3, find the resulting wet-bulb temperature and
relative humidity for 78 F dry-bulb and 52. grains of moisture to be 61.0 F and 37 per
cent, respectively.
e. From the bottom chart, Fig. 4, find the required incoming air temperature to be 42 F
dry-bulb.
13 • Name three factors that influence the feeling of warmth and the elimina-
tion of body heat.
Temperature, humidity, and air movement.
14 • What is meant by effective temperature?
Effective temperature is a composite index which combines the measurements of tem-
perature, air motion, and humidity into a single value. It is an arbitrary index of the
degree of warmth or cold felt by the human body due to these factors.
15 • Referring to the A.S.H.V.E. Comfort Chart (Fig. 3), list the conditions
(dry-bulb, wet-bulb, effective temperature, and humidity) which will produce
comfort at each corner of the average winter comfort zone and of the average
summer comfort zone.
*Heat equivalent of raechaiacal warfc IB foat^poHiwis per Btu,
63
AMERICAS SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
A\erage winter comfort zone:
WET-BULB
DRT-BULB
RELATIVE
F
F
HUMIDITY
58.5
64.5
70 per cent
51.5
67.5
30 per cent
59.0
79.0
30 per cent
67.0
74.0
70 per cent
Average summer comfort zone:
WET-BULB
DRY-BULB
RELATIVE
F
F
HUMIDITY
62.0
68.0 !
70 per cent
54.0
72.0
30 per cent
63.5
: 85.0
30 per cent
71.5
78.5
70 per cent
16 • What is generally considered to be the desirable and practicable range of
relative humidity indoors?
30 per cent to 60 per cent.
64
Chapter 3
INDUSTRIAL AIR CONDITIONING
Moisture Content and Regain, Hygroscopic Materials, Atmos-
pheric Conditions Required? Air Conditioning of Libraries, Banana
Ripening, Lumber Drying, Greenhouse Heating, Apparatus for
Industrial Conditioning
AIR conditioning is applicable to industrial or process conditioning for
the improvement of products during manufacture, or for making the
process independent of climatic conditions. In many industries, the
temperature and relative humidity of the air have a marked influence upon
the rate of production and the weight, strength, appearance, and general
quality of the product. These results are due to the fact that most
materials of animal or vegetable origin, and to a lesser extent minerals in
certain forms, either take up or give moisture to the surrounding air.
MOISTURE CONTENT AND REGAIN
The terms moisture content and regain refer to the amount of moisture
in hygroscopic materials. Moisture content is the more general term and
refers either to free moisture (as in a sponge) or to hygroscopic moisture
(which varies with atmospheric conditions) . It is usually expressed as a
percentage of the total weight of material. Regain is more specific and
refers only to hygroscopic moisture. It is expressed as a percentage of the
bone-dry weight of material. For example, if a sample of cloth weighing
100.0 grains is dried to a constant weight of 93.0 grains, the loss in weight,
or 7.0 grains, represents the weight of moisture originally contained. This
expressed as a percentage of the total weight (100.0 grains) gives the
moisture content or 7 per cent. The regain, which is expressed as a per-
7.0
centage of the bone-dry weight, is ' A or 7.5 per cent.
yo.u
The use of the term regain does not necessarily imply that the material
as a whole has been completely dried out and has re-absorbed moisture.
In the case of certain textiles, for instance, complete drying during manu-
facturing is avoided as it might appreciably reduce the ability of the
material to re-absorb moisture. In measuring moisture it is necessary
to dry out a sample so that the loss in weight may be used as a basis for
calculating the regain of the whole lot.
65
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 1. REGAIN OF HYGROSCOPIC MATERIALS
Moisture Content Expressed in Per Cent of Dry Weight of the Substance at
Various Relative Humidities — Temperature, 75 F
CLASSI-
FICATION
MATERIAL
DESCRIPTION
RELATIVE HUMIDITY— PER CENT
AUTHORITY
10
20
30
40
5.5
50
60
70
80
90
Natural
Textile
Fibres
Cotton
Sea island — roving
2.5
3.7
4.6
6.6
7.9
9.5
11.5
14.1
Hartshorne
| Cotton
American- cloth
2.6
3.7
4.4
5.2
5.9
6.8
8.1
22.8
10.0
14.3
Schloesing
Cotton
Absorbent
4.8
9.0
12.5
15.7
18.5
20.8
24.3
25.8
Fuwa
Woo!
Australian merino — skein
4.7
7.0
8.9
10.8
12.8
14.9
17.2
19.9
23.4
Hartshorne
Silk
Raw ehevennes — skein
3.2
5.5
6.9
8.0
8.9
10.2
11.9
14.3
18.8
Schloesing
Linen
Table cloth
1.9
2.9
3.6
4.3
5.1
6.1
7.0
8.4
10.2
Atkinson
Linen
Dry spun— yarn
3.6
5.4
6.5
7.3
8.1
8.9
9.8
11.2
13.8
Sommer
Jute
Average of several grades
3.1
5.2
6.9
8.5
10.2
12.2
14.4
17.1
20.2
Storch
Hemp
Manila and sisal— rope
2.7
4.7
6.0
7.2
7.9
8.5
9.9
10.8
11.6
13.6
15.7
Fuwa
Bayona
Viscose Nitrocellu-
lose Cupramonium
Average skein
4.0
5.7
6.8
9.2
12.4
14.2
16.0
Robertson
Cellulose Acetate
Fibre
0.8
1.1
1.4
1.9
4.7
2.4
3.0
6.1
3.6
4.3
8.7
5.3
Robertson
Paper
M. F. Newsprint
Wood pulp — 24% ash
2.1
3.2
4.0
5.3
7.2
10.6
U. S. B. of S.
H, M. F. Writing
Wood pulp — 3% ash
3.0
4.2
5.2
6.2
7.2
8.3
9.9
11.9
14.2
13.2
U.S.B.ofS.
White Bond
Rag— 1% ash
2.4
3.7
4.7
5.5
6.5
6.2
7.5
8.8
10.8
U.S. B. ofS.
Com. Ledger
75% rag— 1% ash
3.2
4.2
4.6
5.0
5.6
6.9
8.1
10.3
13.9
U.S.B.ofS.
Kraft Wrapping
Coniferous
3.2
5.7
6.6
7.6
8.9
10.5
12.6
14.9
U.S.B.ofS.
Misc.
Organic
Materials
Leathefr
Sole oak— tanned
5.0
8.5
11.2
13.6
16.0
18.3
20.6
24.0
29.2
Phelps
Catgut
Racquet strings
4.6
7.2
8.6
10.2
6.6
0.44
12.0
7.6
0.54
14.3
17.3
10.7
19.8
21.7
Fuwa
Glue
Hide
3.4
0.11
4.8
0.21
5.8
9.0
11.8
12.5
Fuwa
Rubber
Solid tire
0.32
0.66
0.76
0.88
0.99
Fuwa
Wood
Timber (average)
3.0
4.4
5.9
7.6
9.3
11.3
14.0
17.5
22.0
Forest P. Lab.
Soap
White
1.9
3.8
5.7
7.6
13.3
10.0
12.9
16.1
25.0
19.8
23.8
Fuwa
Tobacco
Cigarette
5.4
8.6
11.0
16.0
19.5
33.5
50.0
Ford
Food-
stuffs
White Bread
0.5
1.7
3.1
4.5
6.2
8.5
11.1
14.5
19.0
Atkinson -
Crackers
2.1
2.8
3.3
3.9
5.0
6.5
13.7
8.3
10.9
14.9
Atkinson
Macaroni
5.1
7.4
8.8
10.2
11.7
16.2
19.0
22.1
Atkinson
Flour
2.6
2.2
4.1
3.8
5.3
6.5
8.0
9.9
12.4
15.4
19.1
Bailey
Starch
5.2
6.4
7.4
8.3
9.2
10.6
12.7
Atkinson
Gelatin
0.7
1.6
2.8
3.8
4.9
6.1
7.6
9.3
11.4
Atkinson
Miac.
Inorganic
Materials
Asbestos Fibre
Finely divided
0.16
0.24
0.26
0.32
0.41
0.51
0.62
0.73
0.84
Fuwa
Silica Gel
5.7
9.8
12.7
15.2
17.2
18.8
20.2
21.5
22.6
Fuwa
Domestic Coke
0.20
0.40
0.61
0.81
1.03
1.24
1.46
1.67
1.89
Selvig
Activated Charcoal
Steam activated
7.1
14.3
22.8
26.2
28.3
29.2
30.0
31.1
32.7
Fawa
Sulphuric Acid
H*SOt
33.0
41.0
47.5
52.5
57.0
61.5
67.0
73.5
82.5
Mason
66
CHAPTER 3 — INDUSTRIAL AIR CONDITIONING
HYGROSCOPIC MATERIALS
Air conditioning is extensively used in the manufacture or processing of
hygroscopic materials such as textiles, paper, wood, leather, tobacco, and
foodstuffs. Where the physical properties of the product affect value, the
question of moisture is of special importance. With increase in moisture
content, hygroscopic materials ordinarily become softer and more pliable.
Economy of manufacturing, therefore, requires that the moisture content
be maintained at a percentage most favorable to rapid and satisfactory
manipulation and to a minimum loss of material through breakage. A
constant condition is desirable in order that high speed machinery may be
adjusted permanently for the desired production with a minimum loss
from delays, wastage of raw material, and defective product.
In the processing of hygroscopic materials, it is usually necessary to
secure a final moisture content suitable for the goods as shipped. Where
the goods are sold by weight it is proper that they contain a normal or
standard moisture content. Air conditioning is important in certain
branches of the chemical industry in controlling the temperature of
reaction and facilitating or retarding evaporation. The control of
moisture content of air supplied to blast furnaces in the manufacture of
pig iron also has proved advantageous.
The moisture content of a hygroscopic material at any time depends
upon the nature of the material and upon the temperature and especially
the relative humidity of the air to which it has been exposed. Not only
do different materials acquire different percentages of moisture after
prolonged exposure to a given atmosphere, but the rate of absorption or
drying out varies with the nature of the material, its thickness and
density.
Table 1 shows the regain or hygroscopic moisture content of several
organic and inorganic materials when in equilibrium at a dry-bulb tem-
perature of 75 F and various relative humidities. The effect of relative
humidity on regain of hygroscopic substances is clearly indicated. The
effect of temperature is comparatively unimportant. In the case of
cotton, for instance, an increase in temperature of 10 deg has the same
effect on regain as a decrease in relative humidity of one per cent. Changes
in temperature do, however, affect the rate of absorption or drying.
Sudden changes in temperature cause temporary fluctuations in regain
even when the relative humidity remains stationary.
Conditioning and Drying
Exposure of hygroscopic materials to an atmosphere of controlled
humidity and temperature for the purpose of establishing a specified
moisture condition in the material is called conditioning. Where the
desired final moisture content is relatively low, the term drying is usually
used- In any case, control of relative humidity, temperature, air velocity
and length of exposure are all of more or less importance.
The conditioning treatment may be undertaken in a special enclosure
(conditioning room) or it may be accomplished in the same room and at
the same time as some regular manufacturing process. For instance, in
the weaving of textiles a high relative humidity is commonly employed to
keep the yarn strong and pHafole* thus assisting in the weaving process and
67
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 2. DESIRABLE TEMPERATURES AND HUMIDITIES FOR INDUSTRIAL PROCESSING
I TEMPERATURE
INDUSTRY PROCESS DEGREES
FAHRENHEIT '
RELATIVE
HUMIDITY
PER CENT
AUTOMOBILE Assembly line 65
40
Cake icing - -
70
50
Cake mixing
75
65
Dough fermentation room
80
76 to 80
Loaf cooling
70
60 to 70
Make-up room
75 to 80
55 to 70
BAKING
*VTixinsr room
75 to 80
1 55 to 70
Paraffin paper wrapping
1 80
55
Proof boxes
80 to 90
80 to 95
Storage of flour
70 to 80
60
I Storage of yeast
28 to 40
60 to 75
BIOLOGIC A.L
Vaccines
' below 32
PRODUCTS
Antitoxins
38 to 42
Fermentation in vat room
44 to 50
50
BREWING
Storasre of strains
60
QA to 4.^
Drying of auger machine brick
180 to 200
Drying of refractory shapes
110 to 150
50 to 60
CERAMIC.-
JVtoldinor room.
80
60
Storage of clay
60
35
CHEMICAL
General storage
60 to 80
35 to 50
Chewing gum rolling
75
50
Chewing gum wrapping
70
45
Chocolate covering
62 to 65
50 to 55
CONFECTIONERY
Hard candy making
70 to 80
30 to 50
Packing
65
50
Starch room
75 to 85
50
Storage
60 to 68
50 to 65
General manufacture
60
45
DISTILLERY
Storage of grains
60
30 to 45
DRUG
Storage of powders and tablets
70 to 80
30 to 35
Insulation winding
104
5
Manufacture of cotton covered wire
60 to 80
60 to 70
ELECTRICAL
Manufacture of electrical win-dings
Storage of electrical goods
60 to 80
60 to 80
35 to 50
35 to 50
Butter making
60
60
Dairy chill room. „
40
60
Preparation of cereals
60 to 70
38
Preparation of macaroni
70 to 80
38
Ripening of meats
40
80
FOOD
Slicing of bacon .
60
45
Storage of apples
31 to 34
75 to 85
Storage of citrus fruit .
32
80
Storage of eggs in shell
30
80
Storage of meats
Oto 10
50
Storage of susar
80
35
Drying of furs
110
FUR
£-», r r
OK 4-f*. Af\
Storage of furs
28 to 40
Zb to 40
68
CHAPTER 3 — INDUSTRIAL AIR CONDITIONING
TABLE 2. DESIRABLE TEMPERATURES AND HUMIDITIES FOR INDUSTRIAL PROCESSING
(Continued)
ISDUSTRT
PROCESS
TEMPERATURE
DEG SITES
FAHBINHEIT
RELATIVE
HUMIDITY
INCUBATORS..
Chicken j 99 to 102 55 to 75
LABORATORY
General analytical and physical-
Storage of materials
60 to 70
60 to 70
60 to 70
35 to 50
LEATHER.-. • Drying of hides..
90
LIBRARY I Book storage (see discussion in thischapter) i 65 to 70 38 to 50
LINOLEUM.- ! Printing
80
40
MATCH..
Manufacturing
Storage of matches..
72 to 74 i
60
50
MUNITIONS Fuse loading
70
Drying of lacquers
60 to 80
25 to 50
PAINT
Drying of oil paints. „
60 to 90
25 to 50
Brush and spray painting
60 to 80
25 to 50
PAPER-
Binding, cutting, drying, folding, gluing..
60 to 80
25 to 50
Storage of paper. _
60 to 80
35 to 45
Development of film
70 to 75
60
Drying . .... ...
75 to 80
50
PHOTOGRAPHIC....
Printing
70
70
Cutting
72
65
Binding
70
45
Folding
77
65
PRINTING
Press room (general) .
75
60 to 78
Press room (lithographic)
60 to 75
20 to 60
Storage of rollers
60 to 80
35 to 45
Manufacturing
90
RUBBER
Dipping of surgical rubber articles
75 to 80
25 to 30
Standard laboratory tests
80 to 84
42 to 48
SOAP
Drying
110
70
Cotton — carding
75 to 80
50
combing — . ..
75 to 80
60 to 65
roving
75 to 80
50 to 60
spinning _
60 to 80
60 to 70
weaving
68 to 75
70 to 80
Rayon — spinning
70
85
TEXTILE..
twisting
70
65
Silk — dressing ..
75 to 80
60 to 65
spinning
75 to 80
65 to 70
throwing
75 to 80
65 to 70
weaving.
75 to 80
60 to 70
Wool — carding _.. . . .
75 to 80
65 to 70
spinning
75 to 80
55 to 60
weaving
75 to 80
50 to 55
Cigar and cigarette making,....
70 to 75
55 to 65
TOBACCO _
Softening
90
85
Stemming or stripping
75 to 85
70
69
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
at the same time leaving the product in a satisfactory condition of regain
for commercial reasons.
As a rule, commercial regain standards are specified percentages which
by test have been found equivalent to a so-called standard atmosphere
with which the goods would be in hygroscopic equilibrium after prolonged
exposure. Committee D13 on Textiles of the American Society for
Testing Materials has adopted a relative humidity of 64 to 66 per cent and
a temperature of 70 to 80 F as the standard atmosphere for textile testing.
ATMOSPHERIC CONDITIONS REQUIRED
The most desirable relative humidity during processing depends upon
the product and the nature of the process. As far as the behavior of the
material itself and its desired final condition are concerned, each material
and process represents a different problem. The best relative humidity
may range up to 100 per cent. Similarly the most desirable temperature
may range between wide limits for different materials and treatments.
Extremes in either relative humidity or temperature require relatively
expensive equipment for maintaining these conditions and controlling
them automatically. Also, in departments where people are working,
their health, comfort, and productive efficiency must be considered. A
compromise often is desirable.
It is generally considered that relative humidities below 40 per cent
are on the dry side, conducive to low regains, a brittle condition of
fibrous materials, prevalence of static electricity, and a tendency toward
dryness of the skin and membranes of human beings. At the other end
of the scale, humidities above 80 per cent are relatively damp, conducive
to high regains, extreme softness, and pliability.
Table 2 lists desirable temperatures and humidities for industrial pro-
cessing. In using this table, care must be taken in qualifying the process.
In preparing many materials, conditions are not maintained constantly,
but different temperatures and humidities are held for varying lengths of
time.
AIR CONDITIONING OF LIBRARIES1
Temperature has little effect on the preservation of books. A tempera-
ture over 100 F, combined with low relative humidity, may cause the book
materials to become brittle, while a temperature much below freezing may
cause permanent deterioration "of the glue in the binding. The relative
humidity should be maintained between 40 and 70 per cent, although
these limits need not hold for short periods of time. If the relative
humidity gets much below 40 per cent, first the glue and then the paper
will tend to become brittle which will not cause any permanent damage
unless the book is used while in this condition, as a subsequent increase
in humidity will bring the materials back to their normal condition. If
the relative humidity gets above 80 per cent, the growth of mildew may
be expected.
One of the principal agents of destruction and deterioration of paper
and books in libraries is sulphur dioxide gas in the air. If air containing
iSec U. S. Bureau of Standards Bulletin No. 128 entitled A Survey of Storage Conditions in Libraries,
by Kimberly and Hicks.
70
CHAPTER 3 — INDUSTRIAL AIR CONDITIONING
sulphur dioxide is allowed to come in contact with cellulose, the principal
constituent of paper, sulphuric acid is formed on the surface. This acid
is not volatile at ordinary temperatures and therefore accumulates
throughout the life of the paper. The destructive effect of the acid on the
paper is independent of the relative humidity of the surrounding air.
Low alkaline concentration spray water may be used in an air washer to
neutralize the acid condition. Such an air washer must be especially
constructed to resist corrosion.
BANANA RIPENING
Ripe bananas are very perishable and for this reason men who deal in
them must depend mainly upon control of the ripening speed as a means
of regulating their daily supply of the fruit. Knowledge and experience
are required in regulating the ripening treatment and to control the
ripening speed. An accurate appraisal must be based upon a careful
examination of the fruit when received to determine its condition, and
periodically, thereafter, to determine the rate of ripening.
Fast ripening may be accomplished in from three to four days after the
green fruit is placed in a ripening room by adjusting the temperatures of
the room until the pulp temperature reaches about 70 F. In wanning up
cool fruit, quick heating is recommended, and it is good practice to use
sufficient heat to raise the average fruit temperature at the rate of 2 to
3 deg per hour. After the first 24 hours, the room should be held at 68 F
until the fruit is colored and then reduced to 66 F and held at this tem-
perature. A high relative humidity of from 90 to 95 per cent should be
maintained until the bananas show color, when it may be reduced to about
80 per cent. High humidity is important during the warming period.
No ventilation should be used until the fruit has colored, after which
ventilation at a rate not to exceed four changes per hour may be used to
assist in reducing the humidity and to freshen the air in the room. If the
fruit shows slow or uneven ripening characteristics, one or two applica-
tions of ethylene gas of approximately 1 cu ft per 1000 cu ft of room space
may be used.
Medium speed ripening of bananas in from five to seven days may be
accomplished by holding the fruit at 64 F. The humidity and ventilation
control should be the same as for fast ripening. A treatment with ethy-
lene gas will seldom be necessary. For slow ripening in from nine to ten
days, the fruit should be held at from 60 to 62 F. Temperatures below
62 F are not advisable for very thin fruit. The humidity should be the
same as for fast ripening, and ventilation (up to 3 or 4 air changes per
hour) should be used provided the humidity can be maintained. Ethylene
gas treatment will not be required.
For holding ripened bananas, temperatures between 56 and 60 F are
recommended. A reduction in humidity is beneficial in toughening the
peel and reducing the mould, but too low a humidity will cause shrinkage.
Although exact humidity control is not essential, the desirable range is
between 75 and 80 per cent.
LUMBER DRYING
The United States Forest Products Laboratory, Madison, Wis., has
71
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
prepared eleven schedules2 for the kiln-drying of practically all kinds,
types, and thicknesses of softwoods and hardwoods. The tables given in
these schedules range from 105 to 200 F dry-bulb, and from 20 to 80 per
cent relative humidity. As a rule, the softer the wood, the higher the
average temperature used. The temperature and relative humidity in a
lumber drying kiln are varied for all conditions, starting with a low dry--
bulb and a high relative humidity when the green lumber, containing a
large percentage of moisture, is started to dry. As the moisture content
of the lumber decreases, the dry-bulb temperature of the kiln is increased,
and the relative humidity reduced. It is noted, however, that perfect
drying does not necessarily result from following a schedule, and that an
operator must be trained to watch the condition of the stock in the kiln
and to immediately apply a remedy if he sees things going wrong.
GREENHOUSES
Table 3 lists customary dry-bulb temperature ranges for different
types of plants and flowers raised in greenhouses.
TABLE 3. CUSTOMARY TEMPERATURES FOR DIFFERENT TYPES OF GREENHOUSES
TYPE OF HOUSE
TEMPERATURE
RANGE
DEGFAHR
TYPE OP HOUSE
TEMPERATURE
RANGE
DEC FA.HR
Carnation -
45 to 55
Orchid, cool
50 to 55
Conservatory (general collection)
60 to 65
Palm, warm
60 to 65
Cool
45 to 50
Palm, cool „
50 to 55
Cucumber
65 to 70
Propagating
55 to 60
Fern „ .
60 to 65
Rose- „
55 to 60
Forcing
60 to 65
Sweet pea
45 to 50
General purpose
55 to 60
Tomato ~
65 to 70
Lettuce
40 to 45
Tropical
65 to 70
Orchid, warm
65 to 70
Violet
40 to 45
APPARATUS FOR INDUSTRIAL CONDITIONING
Apparatus for industrial air conditioning may be divided into two
distinct groups, namely, (1) humidifiers for increasing the moisture con-
tent of the air and for producing cooling by evaporation and (2) dehu-
midifiers for removing moisture from the air and for producing cooling by
contact with water or surfaces at a lower temperature than the air.
Strictly speaking, humidity control alone, whether it involves humidi-
fication or dehumidification, is not air conditioning. To be entitled to this
classification according to the definition in Chapter 41, the process should
include the simultaneous control of temperature, humidity and air motion.
Industrial humidifiers may be divided into the following general
types, according to the method of operation :
1. Direct, which spray into the room.
2. Indirect, which introduce moistened air.
3. Combined direct and indirect.
-Technical Note Number 1 7o, Forest Products Laboratory, U. S. Forest Service, Madison, Wis.
72
CHAPTER 3 — INDUSTRIAL AIR CONDITIONING
Spray Generation
Spray generation is obtained by (1) atomization, (2) impact, (3)
hydraulic separation, and (4) mechanical separation.
Atomization involves the use of a compressed air jet to reduce the water
particles to a fine spray. With the impact method, a jet of water under
pressure impinges directly on the end of a small round wire. Where
hydraulic separation is employed, a jet of water enters a cylindrical
chamber and escapes through an axial port with a rapid rotation which
causes it immediately to separate in a fine cone-shaped spray. In the
mechanical separation process, water is thrown by centrifugal force from
the surface of a rapidly revolving disc and separates into particles suf-
ficiently small to be utilized in certain types of mechanical humidifiers.
Spray Distribution
Spray distribution is obtained by (1) air jet, (2) induction, and (3) fan
propulsion.
The air jet which generates the spray in atomizers also carries the spray
through a space sufficient for its distribution and evaporation, and this
method of distribution is termed air jet. Where distribution is obtained
by induction, the aspirating effect of an impact or centrifugal spray jet is
utilized to induce a current of air to flow through a duct or casing, and
this air current distributes the spray. Fan propulsion obviously consists
of the utilization of fans to entrain and distribute the spray.
Industrial type direct humidifiers are commonly classified as (1)
atomizing, (2) high-duty, (3) spray and (4) self-contained or centrifugal.
Atomizing Humidifiers
There are several types of atomizing humidifiers, all of which rely upon
compressed air as the atomizing and distributing agency, similar to the
familiar method used in ordinary nasal atomizers. Compressed air
(ordinarily about 30 Ib per square inch) is supplied from a centrally-
located air compressor through pipe lines to the atomizing units. The air
lines are usually horizontal and parallel to water lines which supply
water by gravity from a float tank. The water in the tank is maintained
at a constant level slightly lower than the outlets of the atomizers them-
selves and is drawn constantly to the atomizer by aspiration when com-
pressed air is supplied. This aspiration ceases and the flow of water stops
when the air supply is cut off. The water should not be supplied under
pressure to atomizers because of the possibility of leakage, drip, or coarse
spray which cannot be permitted when water is supplied by aspiration.
High-Duty Humidifiers
Water is supplied to high-duty humidifiers under high pressure (usually
about 150 Ib per square inch) through pipe lines from a centrally-located
pumping unit. The spray-generating nozzle which is of the impact type
is located in a cylindrical casing, A drainage pan provides for the collec-
tion and return of unevaporated water which flaws through a return pipe
to a filter tank, from which it is recirculated. A powerful air current is
forced through the humidifier by means of a fan mounted above the unit.
73
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
The air enters from above, is drawn through the head, charged with
moisture, and cooled to the wet-bulb temperature. It then escapes from
the opening below at a high velocity in a complete and nearly horizontal
circle. The spray is quickly evaporated and the resulting vapor is rapidly
and thoroughly diffused. This effective distribution of fine spray over
the maximum possible area insures complete and extremely rapid vapori-
zation even at the highest humidities.
Spray Humidifiers
This type of humidifier consists of an impact spray nozzle in a cylin-
drical casing with a drainage pan below it. The aspirating effect of the
spray nozzle induces a moderate air current through the casing which
distributes the entrained spray. The general method of circulating and
returning the water is similar to that employed for high-duty humidifiers.
A suitable pump and centrally-located filter tank are required.
The spray and high-duty types of humidifiers have many features in
common but the latter, because of its finer spray and greater capacity,
is often considered better adapted for producing high humidities.
Self-Contained Humidifiers
The self-contained or centrifugal humidifier has the ability to generate
and distribute spray without the use of air compressors, pumps, or other
auxiliaries. These may be used either singly or in groups. In large
installations, where suitable connections are provided to permit the
cleaning and servicing of individual units without affecting the room as a
whole, group control of the water and power may be employed.
Humidifiers and air washers are also described in Chapter 11.
Where large quantities of power are generated in a limited space and
where a comparatively high relative humidity is required, it is often
feasible and economical to use a combination of direct and indirect
humidification. The indirect humidification provides the desired quantity
of ventilation and cooling, and the additional direct humidification pro-
vides for increase in humidity without interfering with the ventilation or
the cooling effected by the indirect system.
In general, it may be stated that direct humidification is most satis-
factory where high humidities are desired but where little cooling, ven-
tilation or air motion is required. Therefore, the indirect system is most
applicable where either low or high relative humidities are desired with
maximum cooling and ventilation effect. For conditions that require an
unusually large amount of heat to be absorbed by ventilation, together
with the maintenance of high humidities, it is often preferable to make
use of the combination system of indirect and direct humidification. If
the indirect system alone were used it would mean an unusually large
volume of air to be handled, which might interfere, due to air motion,
with production, even though it would result in greater cooling effect. If
direct humidification alone were used, no ventilation would be obtained,
with consequently higher room temperatures.
Dehumidifiers, which are similar in design and appearance to indirect
humidifiers and air washers, are described in Chapter 11. The main
differences are found in the internal construction of the dehumidifier, in
74
CHAPTER 3 — INDUSTRIAL AIR CONDITIONING
the use of refrigeration or of heat as required for controlling the water
temperature, and in differences in the general methods of control.
PROBLEMS IX PRACTICE
1 • A condition of 75 F dry -bulb temperature and 55 per cent relative humidity
is being maintained in a cigarette manufacturing department. What will be
the regain and moisture content of the tobacco?
The regain, from Table 1 = 17,75 per cent.
~, . 17.75 X 100
The moisture content = r^ . .,-,-;- = lo.l per cent.
100 4- 17./O
2 • A 1-lb sample taken from a 100-lb batch of material is found to have a bone
dry weight of 0.89 Ib. This material is to be processed under atmospheric
conditions which should produce a regain of 15 per cent. Compute the finished
weight for each original 100-lb batch.
Let W equal the number of pounds of moisture in a finished batch.
W „ ,15
gg- regain -lo per cent -jgg
W = 13.35
89 + 13.35 = 102.35 Ib finished weight.
3 • A bundle of sea island cotton is found to have a bone dry weight of 9.26 Ib-
What is the proper relative humidity at 75 F to produce a weight of 10 Ib at
equilibrium?
Desired conditioned weight = 10.00 Ib
Bone dry weight = 9.26 Ib
Weight of moisture required = 0.74 Ib
074
Regain = -~ X 100 = 7.9 per cent.
From Table 1, the proper relative humidity required is 60 per cent.
4 • Compute tlie bone dry weight of 1000 Ib of manila rope which has been,
stored for a considerable period of time in a conditioned room at 75 F dry-bulb
temperature and 50 per cent relative humidity.
Assuming that this material has come to equilibrium under the atmospheric conditions
given, Table 1 shows a regain of 8.5 per cent.
Let W equal the total weight of moisture in pounds.
1000 — W — bone dry weight in pounds.
= regain =8.5 per cent
1000 - W ^ ^ 100
W = 78.3 Ib moisture
1000 - 78.3 = 921.7 Ib bone dry weight.
5 • An egg evaporating plant wishes to dry 2000 Ib of egg whites (85 per cent
water) to crystalline form each 24 hours* The nmyimmm permissible air de-
livery temperature in the dryer is 140 F. What air volume will be required,
assuming that outside air is at 95 F dry-bulh and 78 F wet-bulb and that air
leaves the dryer 70 per cent saturated?
Moisture to be removed = 2000 X 0.85 = 1700 Ib. Using psychroroetric chart and
starting at the intersectioH of the vertical 95 F dry-bulb temperature line and the 45 per
cent humidity Ene, move horizontally to tlie right to the intersection with the 140 F
vertical temperature line at 10 per cewt relative haxmdHy ; then inove along the constant
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
heat 'or wet-bulb line; to its intersection with the 70 per cent relative humidity curve
and read 94 F dry-bulb, which will be the temperature of the air leaving the dryer.
Moisture per cubic foot at 94 F and 70 per cent relative humidity = 11.8 grains
Moisture per cubic foot at 95 F and 78 F wet-bulb = 8.0 grains
Moisture added per cubic foot of air handled = 3.8 grains
1700 X 7000
No allowance is made for heat lost in the transmission to and from the dryer or for the
heat required to raise the product from its entering temperature to that maintained in the
dryer. This would necessitate a trial and error solution common to all drying problems.
6 • It is proposed to install a central fan type air conditioning system com-
prised of fan, air washer, filters, and heating coils to provide ventilation and to
maintain proper humidity in a small library during periods of winter operation.
The heat loss has been estimated at 450,000 Btu per hour in maintaining a
condition of 72 F dry-bulb and 45 per cent relative humidity. Assuming that
the air washer completely saturates the air, what must be the leaving dry-and
wet-bulb temperatures to provide the required condition?
49.85 F is the dew-point temperature corresponding to the stated required condition,
7 • Assuming a maximum permissible air delivery temperature of 100 F in
Question 6, what air volume will be required?
450,000 X 55.2
(100 - 72) X 60
14,800 cfm.
8 • If in Questions 6 and 7 it is assumed that winter humidity control will
consist simply of a dew-point thermostat at the exit of the air washer, control-
ling the dew-point temperature by operating automatic dampers, and thereby
proportioning the respective volumes of outside and recirculated air admitted:
a. What volume of air should be recirculated?
b. What volume of air will be exfiltrated from the buildings?
c. What reheating capacity will be required?
a. Btu per pound at 72 F and '45 per cent relative humidity = 25.38
Btu per pound at 0 F (assumed saturated) = 0.85
Btu per pound at 49.85 F saturated = 20.11
Recirculated air = ^5 38 ~ 0 85) X 14'8°° = 11'6°° cfm*
b. The same volume as is introduced as fresh outside air, namely,
14,800 - 11,600 = 3200 cfm.
c. The reheaters must be of such capacity as to reheat the volume of air
handled from 49.85 (the dew-point) to 100 F.
14,800 X (100 - 49.85) X 60
55.2
= 808,000 Btu per hour.
76
Chapter 4
NATURAL VENTILATION
Wind Forces, Stack Effect, Openings, Windows, Doors, Skylights,
Roof Ventilators, Stacks, Principles of Control, General Rules,
Measurements, Dairy Barn Ventilation, Garage Ventilation
VENTILATION by natural forces, supplemented in certain cases
with mechanical forces, finds extensive application in industrial
plants, public buildings, schools, dwellings, garages, and in farm buildings.
The natural forces available for the displacement of air in buildings are
the wind and the difference in temperature of the air inside and outside
the building. The arrangement and control of ventilating openings
should be such that the two forces act cooperatively and not in opposition,
Wind Forces
In considering the use of natural wind forces for the operation of a
ventilating system, account must be taken of (1) average and minimum
wind velocities, (2) wind direction, (3) seasonal, daily and hourly varia-
tions in wind velocity and direction, and (4) local wind interference by
buildings and trees.
Table 1, Chapter 8, gives values for the average summer wind velocities
and the prevailing wind directions in various localities throughout the
United States, while Table 2, Chapter 7, lists similar values for the winter.
In almost all localities the summer wind velocities are lower than those in
the winter, and in about two-thirds of the localities the prevailing direc-
tion is different during the summer and winter. While average wind
velocities are seldom below 5 mph, there are many hours in each month
during which the wind velocity is from 3 to 5 mph, even in localities where
the seasonal average is considerably above 5 mph. There are relatively
few places where the hourly wind velocity falls much below 3 mph for
more than 10 daylight hours per month. Usually a natural ventilating
system should be designed to operate satisfactorily with a wind velocity
of 3 to 6 mph, depending on locality.
The following formula may be used for calculating the quantity of air
forced through ventilation openings by the wind, or for determining the
proper size of such openings:
Q = EA V (1)
where
Q = air flow in cubic feet per minute. _
A — free area of inlet (or outlet) openings in square feet.
V — wind velocity in feet per minute,
— miles per hour X 88.
E = effectiveness of openings.
(R sfconld be taken at from 50 to 60 per cent if the inlet openings face the wind and from 25 to 35 per
cent if the infet openinigs receive tfoe wirad at an angle.)
in
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
If outlet openings, where air leaves a building, are smaller than inlet
openings, where air enters a building, the air will be less effective than
indicated by the constant E.
The accuracy of the results obtained by the use of Formula 1 depends
upon the placing of the openings, as the formula assumes that ventilating
openings have a flow coefficient slightly greater than that of a square-edge
orifice. If the openings are not advantageously placed with respect to the
wind, the flow per unit area of the openings will be less, and if unusually
well placed, the flow will be slightly more than that given by the formula.
Inlets should be placed to face directly into the prevailing wind, while
outlets should be placed in one of the following four places :
1. On the side of the building directly opposite the direction of the prevailing wind.
2. On the roof in the low pressure area caused by the jump of the wind (see Fig. 1).
3. In a monitor on the side opposite from the wind.
4. In roof ventilators or stacks exposed to the full force of the wind1.
Forces due to Stack Effect2
The stack effect produced within a building is due to the difference in
weight of the warm column of air within the building and the cooler air
outside. The flow due to stack effect is proportional to the square root
of the draft head, or approximately:
Q - 9.4 A V H (ti - *2) (2)
where
Q — air flow in cubic feet per minute.
A = free area of inlets or outlets (assumed equal) in square feet.
H — height from inlets to outlets, in feet.
ti — average temperature of indoor air in height H, in degrees Fahrenheit.
/2 = temperature of outdoor air, in degrees Fahrenheit.
9.4 ss constant of proportionality, including a value of 65 per cent for effectiveness of
openings. This should be reduced to 50 per cent (constant = 7.2) if conditions
are not favorable.
The height between inlets and outlets should be the maximum which
the building construction will allow.
In some cases the necessary air flow will be known from the require-
ments of the building occupancy, and the area necessary for certain
assumed temperature differences may be calculated. Or the areas may
be fixed by the building construction, and the maximum air flow for
various differences between indoor and outdoor temperatures may be
calculated. In any case, the conditions which give the minimum air flow
are those which control the design, as the system must have ample
capacity even under the most unfavorable conditions which are those of
mild or warm weather.
TYPES OF OPENINGS
The engineering problems of a natural ventilation system consist of the
design, location, and control of ventilating openings to best utilize the
'See Airation of Industrial Buildings, by W. C. Randall (A.S.H.V.E. TRANSACTIONS, Vol. 34, 1928).
2See Neutral Zone in Ventilation, by J. E. Emswiler (A.S.H.V.E. TRANSACTIONS, Vol. 32, 1926), and
Predetermining Airation of Industrial Buildings, by W. C. Randall and E. W. Conover (A.S.H.V.E. TRANS-
ACTIONS, Vol. 37, 1931).
78
CHAPTER 4 — NATURAL VENTILATION
natural ventilation forces, in accordance with the requirements of build-
ing occupancy. The types of openings may be classified as:
1. Windows, doors, monitor openings, and skylights.
2. Roof ventilators.
3. Stacks connecting to registers.
4. Specially designed inlet or outlet openings.
Windows, Doors and Skylights
Windows have the advantage of transmitting light, as well as providing
ventilating area when open. Their movable parts are arranged to open in
FIG. 1. THE JUMP OF WIND FROM WINDWARD FACE OF BUILDING. (A— LENGTH or
SUCTION AREA; B — POINT OF MAXIMUM INTENSITY OF SUCTION;
C — POINT OF MAXIMUM PRESSURE)
various ways; they may open by sliding as in the ordinary double-hung
windows, by tilting on horizontal pivots at or near the center, or by
swinging on pivots at the top or bottom. Whatever the form and type of
window used, the amount of dear area that can be made available is the
factor of greatest importance in ventilation.
All types of sash (double-hung, top, center or bottom horizontal pivoted,
or vertical pivoted) have about the same air flow capacity for the same
clear area. Air leakage through dosed windows is important during high
winds (Chapter 6).
7§
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
The proper distribution of air in occupied spaces is an element almost
as important as that of sufficient air quantity. Advantageous pivoting of
sash is very useful for securing good air distribution. Deflectors are some-
times used for the same purpose, and these devices should be considered a
part of the ventilation system.
Door openings are seldom included in the ventilation calculations,
though they may be of great value for extreme summer conditions, and
should be considered in this connection as well as in garage design.
Skylight and monitor openings are of importance as these and the roof
ventilators are outlets, while the lower windows are usually inlets on the
windward side and outlets on the leeward side. In general the areas of
inlets and of outlets should be about equal. It is important to make a
check on this ratio in any installation, as any great excess of area of one
set of openings over another means waste opening area. The operating
devices used for sash, monitors, skylights and roof ventilators should be
well selected as poor operating devices may defeat the entire design.
Roof Ventilators
The function of a roof ventilator is to provide a storm and weather
proof air outlet, which is sensitive to wind action for producing additional
flow capacity, and at the same time is subject to manual or automatic
control by suitable dampers. The capacity of a ventilator at a constant
wind velocity and temperature difference, depends upon four things:
(1) its location on the roof, (2) the resistance it offers to air flow, (3) the
area and location of openings provided for air inflow at a lower level, and
(4) the ability of the ventilator head to utilize the kinetic energy of the
wind for inducing flow by centrifugal or ejector action. Frequently one
or more of these capacity factors is overlooked in a ventilator installation.
For maximum flow induction, a ventilator should be located on that
part of the roof which receives the full wind without interference. (See
Fig. 1.) This does not mean that no ventilators are to be installed within
the suction region created by the wind jumping over the building, or in a
light court, or on a low building between two high buildings. Ventilators
are highly effective in such low-pressure areas, but their ejector action,
caused by wind velocity, is of little importance in these locations, and
hence their size should be increased proportionally.
Ventilator resistance depends on (1) type of inlet, (2) area of openings
and passages, and (3) number of turns or changes of direction of the air
flow. The inlet grille, if any, should have ample free area, and the venti-
lator should always be provided with a taper-cone inlet in order to produce
the effect of a bell-mouth nozzle (flow coefficient 0.97) rather than that of
a square-entrance orifice (flow coefficient 0.60) . In other words, the grilles
should be oversize as compared with the ventilator, and they should be
connected by tapering collars. If the ventilator head construction
produces changes in the direction of air flow, the area of the flow passages
should be increased accordingly.
Air inlet openings at lower levels in the building are of course necessary
for the economical use of ventilator capacity. The inlet openings should
be at least equal to, and preferably twice as great as the combined throat
areas of all roof ventilators. The air discharged by a roof ventilator
80
CHAPTER 4 — NATURAL VENTILATION
depends on wind velocity and temperature difference, but due to the four
capacity factors already mentioned, no simple formula can be devised for
expressing ventilator capacity.
Several types of roof ventilators are shown in Figs. 2 to 11. These may
be classified as stationary, Figs. 2 to 6, pivoted or oscillating, Figs. 7 to 9,
or rotating, Figs. 10 and 11. When selecting unit ventilators, some
attention should be paid to ruggedness of construction, storm-proofing
features, dampers and damper operating mechanisms, possibilities of
noise from dampers or other moving parts, and possible maintenance
costs.
It should be kept in mind that a suitable combination of roof venti-
lators with mechanical ventilation frequently offers the best solution of a
ventilating problem. The natural ventilation units may be used to sup-
plement power driven supply fans, and under favorable weather con-
ditions it may be possible to shut down the power driven units. Where
low operating costs are very important, such a combination has great
advantages. Roof ventilators with built-in electric fans are attracting
increased attention because they combine the advantages of low instal-
lation and operating cost with those of continuous service.
Controls
In connection with any combination between natural and fan venti-
lation, the controls are of importance. Both the fans and the ventilator
dampers may be controlled by some combination of three methods:
(1) hand operation, (2) thermostat operation, and (3) control by wind
velocity. The thermostat station may be located anywhere in the
building, or it may be located within the ventilator itself. The purpose of
wind velocity control is to obtain a definite volume of exhaust regardless
of the natural forces, the fan motor being energized when the natural
exhaust capacity falls below a certain minimum, and again shut off when
the wind velocity rises to the point where this minimum volume can be
supplied by natural forces.
Stacks
Stacks are really chimneys and utilize both the inductive effect of the
wind and the force of temperature difference (the so-called gravity action).
While their openings projecting above the roof are not provided with any
special construction for developing suction by the action of the wind, the
plain vertical opening is also effective in this respect. Like the roof
ventilator, the stack outlet should be located so that the wind may act
upon it from any direction.
Stacks are applicable particularly in the case of schools, apartments,
residences and small office buildings. Partitions interfere with general
air circulation, and some type of outlet from each room is necessary. If
the building is not too tall, and the requirements of occupancy are moder-
ate, a system of stacks with registers in each room may be more eco-
nomical than a system of mechanical ventilation employing fans. In
making the comparison, however, the building space occupied by the
stacks should be considered.
With little or no wind, chimaey effept or temperature difference will
produce outflow through the stacks and an equal inflow through windows
81
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
( 1
I
/
^* '
A
—
^™
71
JP
f
\* ^
N
r V_
af
£.—
_J> ^
X
FIG. 2
FIG. 3
FIG. 4
FIG. 5 FIG. 6
Six. COMMON TYPES OF STATIONARY VENTILATORS
FIG. 7 FIG. 8 FIG. 9
THREE TYPICAL OSCILLATING VENTILATORS
82
CHAPTER 4 — NATURAL VENTILATION
in all sides of the building. With wind, the inductive* force at the top of
ventilating shafts is more powerful than that on the leeward side of the
building, so that air is drawn in through leeward openings by a combina-
tion of the forces of wind and temperature difference. On the windward
side, the direct forcing pressure of the wind is of course added to the
temperature difference effect. Thus forces are available for causing in-
flow at practically every window of such a building. Adequacy of stack
size must, of course, be provided.
PRINCIPLES OF AIR FLOW CONTROL
The air flow through a ventilation opening depends on the two factors
already discussed, namely, (1) the natural forces available, (2) the open-
ings available, and the resistance to flow offered by these openings. The
design problem includes, of course, a determination of the desired air
/ Propelling blai
FIG. 10.
SE.OTIOM
ROTATING VENTILATORS
FIG. 11.
quantity and distribution in order that the openings may be properly
placed.
The purpose of ventilation is to carry off either excess heat or air
impurities, and the desired air quantities depend upon the amount of heat
or of impurities present. The amount of heat can be determined, in the
case of forge shops for example, from the amount of fuel burned, which in
turn is based upon the production capacity for which the building is
being designed. In the case of foundries, the heat given off by the metal
in cooling from the molten state can be used. In some instances, not all
of the heat may be dissipated to the air, but a fair estimate of the amount
to be removed by the air can usually be made.
The next step is to select the temperature difference to be maintained.
Knowing the amount of heat to be removed and having selected a
desirable temperature difference, the amount of air to be passed through
the building per minute to maintain this temperature difference can be
determined by means of the following equation :
H
where
cQD
V
(3)
c ~ 0.24 = specific heat of air.
V — specific volume of the air, cubic feet per pound, about 13.5. (See Chapter 41.)
83
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
H = heat to be carried off, in Btu per minute.
Q — air flow in cubic feet per minute.
D = inlet-outlet temperature difference in degrees Fahrenheit.
For disposing of air impurities, the required air flow must be such that
the outside air will dilute the impurities to a degree that they are no
longer objectionable. For human occupancy, such as in auditoriums and
classrooms, 10 cfm per person is usually taken as the minimum of outside
air necessary for ventilation (see Chapter 2). For garage ventilation,
sufficient air must be admitted to dilute the carbon monoxide content of
the indoor air to 1 in 10,000 (see Garage Ventilation in this Chapter).
Air quantity and quality are not the only requirements. For human
occupancy, air distribution is important. In ventilation the air distribu-
tion is almost entirely a matter of the number, the design, and the location
of inlets and outlets. In locating openings, special precautions should be
taken against the formation of dead air spaces or pockets within the zone
of occupancy.
Suggested methods for estimating the air flow due to temperature
difference alone and to wind alone have already been given. It must be
remembered that when both forces are acting together, even without
interference, the resulting air flow is not equal to the sum of the two
estimated quantities. The same openings have been assumed in both
cases, and since the resistance to flow through the openings varies ap-
proximately with the square of the velocity3, this resistance becomes a
limiting factor as the flow through the openings is increased.
Recent investigations1* 2 show that the total flow is only 10 per cent
above the flow caused by the greater force when the two forces are nearly
equal, and this percentage decreases rapidly as one force increases above
the other. Tests on roof ventilators indicate that this is too conservative
in the direction of low total flow quantities, but there is in any case a
large judgment factor involved. The wind velocity and direction, the
outdoor temperature, or the indoor activities cannot be predicted with
certainty, and great refinement in calculations is therefore not justified.
When designing for winter conditions, an added variable is the heat lost
by direct flow through walls and windows and by infiltration.
Example 1. Assume a drop forge shop, 200 ft long, 100 ft wide, and 30 ft high. The
cubical content is 600,000 cu ft, and the height of the air outlet over that of the inlet is
30 ft. Oil fuel of 18,000 Btu per Ib is used in this shop at the rate of 15 gal per hour
(7.75 Ib per gal) . Temperature differences are 10 F in summer and 30 F in winter, and
the wind velocity is 5 mph in summer and 8 mph in winter. What is the necessary area
for the inlets and outlets, and what is the rate of air flow through the building?
Solution. The system must be designed for the summer conditions as these are the
more severe. The heat to be removed per minute is:
H - ^- X 7.75 X 18,000 - 34,875 Btu.
uu
By Equation 3, the air flow required to remove this heat with a temperature difference
of 10 deg is:
VH 13.5 X 34,875 .
Q = -& 0.24X10 = 1
This is true for turbulent flow only. It would be more correct to state that the resistance varies approxi-
mately with V2 for high to moderate velocities, with F1'8 for moderate to low velocities, and with the first
power of the velocity for very low velocities through small openings.
84
CHAPTER 4 — NATURAL VENTILATION
This is equal to 19.6 air changes per hour. The assumption is made that the average
temperature difference between indoors and outdoors is the same as the temperature rise
of the air from the inlet opening to the outlet opening. Actually, the latter difference is
larger and so the value of 19.6 air changes per hour is conservative as it allows for more
cooling than is necessary for an average temperature difference of 10 deg.
If 196,172 cfm are to be circulated by the force of the temperature difference alone, the
area of opening would be, by Equation 2:
196,172
If this area of openings were provided, a wind velocity of 5 mph, acting alone, would
produce a flow according to Equation 1, of:
<2 « EA V = 0.50 X 1,205 X 5 X 88 = 265,100 cfm.
If the inlet openings^do not face the wind, but are at an angle with it, about half this
amount may be considered to flow.
A factor of judgment must now be exercised in making the selection of
the area of openings to be specified. Apparently 1205 sq ft are a very
generous allowance because either a direct wind of 5 mph or an average
temperature difference of 10 deg acting alone will more than suffice to
carry away the heat, and when the two forces are acting together, the
system may have an excess capacity of 25 per cent to 50 per cent, especially
if the outlets are made up partially of roof ventilators which employ the
force of the wind for producing a suction effect. On the other hand, the
wind may at times come from an unfavorable direction, or its velocity
may fall below 5 mph or the building construction may not permit a full
2400 sq ft of inlet window area and an equal amount of monitor or roof
ventilator outlet area. In case the two sets of openings are not equal,
their effectiveness is reduced.
From this example it must be apparent that while formulas may
furnish a reliable guide, the final solution of a problem of natural venti-
lation requires a common sense analysis of local conditions to supplement
and to modify the dictates of the formulas.
GENERAL RULES
A few of the important requirements in addition to those already
outlined are:
1. Inlet openings should be well distributed, and should be located on the windward
side near the bottom, while outlet openings are located on the leeward side near the top.
Outside air will then be supplied to the zone of occupancy.
2. Direct short circuits between openings on two sides at a high level may clear the
air at that level without producing any appreciable ventilation at the level of occupancy.
3. Roof ventilators should be located 20 to 40 ft apart each way and preferably on
the ridge of the roof. The closer spacings are used when ventilating rooms with low
ceilings.
4. Greatest flow per square foot of total opening is obtained by using inlet and outlet
openings of nearly equal areas.
5. In an industrial building where furnaces, that give off heat and fumes, are to be
installed, it is better to locate them in the end of the building exposed to the prevailing
wind. The strong suction effect of the wind at the roof aear the windwajrd end will then
cooperate with temperature difference, to provide for the most active and satisfactory
removal of the heat and gas laden air.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
6. In case it is impossible to locate furnaces in the windward end, that part of the
building in which they are to be located should be built higher than the rest, so that
the wind, in splashing therefrom will create a suction. The additional height also
increases the effect of temperature difference to cooperate with the wind.
7. In the use of monitors, windows on the windward side should usually be kept
closed, since, if they are open, the inflow tendency of the wind counteracts the outflow
tendency of temperature difference. Openings on the leeward side of the monitor result
in cooperation of wind and temperature difference.
8. In order that the force of temperature difference may operate to maximum advan-
tage, the vertical distance between inlet and outlet openings should be as great as
possible. Openings in the vicinity of the neutral zone are less effective for ventilation.
9. In order that temperature difference may produce a motive force, there must be
vertical distance between openings. That is, if there are a number of openings available
in a building, but all are at the same level, there will be no motive head produced by
temperature difference, no matter how great that difference might be.
10. In the design of window ventilated buildings, where the direction of the wind is
quite constant and dependable, the orientation of the building together with amount
and grouping of ventilation openings can be readily arranged to take full advantage of
the force of the wind. On the other hand, where the direction of the wind is quite
variable, it may be stated as a general principle that windows should be arranged in
sidewalls and monitors so that there will be approximately equal area on all sides.
Thus, no matter what the wind 's direction, there will always be some openings directly
exposed to the pressure force of the wind, and others opposed to a suction force, and
effective movement through the building will be assured.
11. The intensity of suction or the vacuum produced by the jump of ^the wind is
greatest just back of the building face. The area of suction does not vary with the wind
velocity, but the flow due to suction is directly proportional to wind velocity.
12. Openings much larger than the calculated areas are sometimes desirable, especially
when changes in occupancy are possible, or to provide for extremely hot days. In the
former case, free openings should be located at the level of occupancy for psychological
reasons.
13. Special consideration should be given to the possibility of sidewall or monitor
windows being closed on account of weather conditions. Such possibilities favor roof
ventilators and specially designed stormproof inlets.
MEASUREMENT OF NATURAL AIR FLOW
The determination of the performance of any ventilating system
involves measurements which are not easy to make. The difficulties are
increased in the case of natural ventilation, since the motive forces and
the air velocities are very small. The measurements necessary for giving
the capacity of a system are (1) velocity of the wind, (2) velocity of the
air through inlet and outlet openings, (3) outdoor air temperature, and
(4) average indoor air temperature.
Measuring Wind Velocity. The cup-type of anemometer as used for
Weather Bureau observations is sufficiently accurate for this measure-
ment. Some more accurate instruments as well as direct-reading types
have been developed for airport service, but for ventilation work it is the
average wind velocity over a long period which determines the capacity of
the system. Hence the use of the Weather Bureau instrument, with an
observation period of one hour or more, is satisfactory. If observations
of wind direction are required, these should be taken by observing a
sensitive weather vane at frequent intervals (about every 5 minutes)
during the same period,
Velocity of Air Through Openings. The vane type anemometer is the
most practical instrument for this measurement.
86
CHAPTER 4 — NATURAL VENTILATION
Use a small (4 in.) low-speed anemometer, and correct all readings
according to a recent calibration. Mount the anemometer in a strap iron
clamp with a long handle for convenience. Divide each opening into
5 in. squares (by string or wire) and hold the anemometer in the center of
each square for a definite period of from 15 to 30 seconds. Record the
result of the traverse as soon as completed and start another one im-
mediately. A series of traverses over a period of one hour, or the full
period covered by the wind velocity observations with a fairly steady
wind, may be considered a satisfactory test for that wind velocity. It is
preferable to have an anemometer observer at each opening. If the
opening is covered by a grille or register, use the proper correction factors
(see Chapter 40).
Outdoor Temperature. It is easy to make an error of 1 to 5 deg in
observing ^the outdoor _ air temperature. An accurate thermometer,
calibrated in 1 deg divisions should be used. The thermometer should be
mounted in the shade at about mid-height of the building and not too
near the building wall or adjacent to an air outlet. The heat from a wall
or roof which has been exposed to the sun is easily transmitted to a
thermometer, with resulting high readings.
Average Indoor Temperature. It is important to note that the capacity
of an opening (such as roof ventilator) does not depend on the difference
in the temperatures measured adjacent to the opening. It depends
rather on the difference between the average temperature of the column
of air inside the building and that outside. Indoor temperatures should
therefore be observed at various heights to secure a good average.
DAIRY BARN VENTILATION4
A successful barn ventilating system is one which continuously supplies
the proper amount of air required by the stock, with proper distribution
and without drafts, and one which removes the excessive heat, moisture,
and odors, and maintains the air at a proper temperature, relative
humidity, and degree of cleanliness.
Barn temperatures below freezing and above 80 F affect milk produc-
tion. Milk producing stock should be kept in a barn temperature be-
tween 45 and 50 F. Dry stock, at reduced feeding, may be kept in a barn
5 to 10 deg higher. Calf barns are generally kept at 60 F, while hospital
and maternity barns usually have a temperature of 60 F or somewhat
higher.
The heat produced by a cow of an average weight of 1000 Ib may be
taken as 3000 Btu per hour. The average rate of moisture production by
a cow giving 20 Ib of milk per day is 15 Ib of water per day, or 4375 grains
per hour. To set a standard of permissible relative humidity for cow
barns is difficult. For 45 F an average relative humidity of 80 per cent
is satisfactory, with 85 per cent as a limit.
Where the barn volume is within the limit that can be heated by the
stabled animals, the air supply need not be heated. The air should be
*For additional information on this subject refer to Technical Bulletin, U. S, Department of Agriculture
(1930), by M. A. R. Kelley.
Dairy Barn Ventilation, by F. L. Fairbanks (A.S.H.V.E. TRANSACTIONS, Vol. 34, 1928).
Cow Barn Ventilation, by Alfred J. Offner (A^S.H.V.E. Journal Section, Heating, Piping and Air
Conditioning. January, 1933).
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
supplied through or near the ceiling. It is better to have the exhaust
openings near the floor as larger volumes of warm air are then held in the
barn and there is better temperature control with less likelihood of sudden
change in barn temperature.
If a cow weighs 1000 Ib and produces 3000 Btu of heat per hour, and if
a barn for the cow has 600 cu ft of air space with 130 sq ft of building
exposure, one cow will require 2600 to 3550 cfh of ventilation, depending
on the temperature zone in which the barn is located. The permissible
heat losses through the structure, based on one cow and depending on the
temperature zone, vary between 0.043 and 0.066 Btu per hour per cu ft
of barn space, and 0.197 to 0.305 Btu per hour per sq ft of barn exposure.
GARAGE VENTILATION-6
On account of the hazards resulting from carbon monoxide and other
physiologically harmful or combustible gases or vapors in garages, the
importance of proper ventilation of these buildings cannot be over-
emphasized. During the warm months of the year, garages are usually
ventilated adequately because the doors and windows are kept open. As
cold weather sets in, more and more of the ventilation openings are closed
and consequently on extremely cold days the carbon monoxide concentra-
tion runs high.
Many garages can be satisfactorily ventilated by natural means par-
ticularly during the mild weather when doors and windows can be kept
open. However, the A.S.H.V.E. Code for Heating and Ventilating
Garages, adopted in 1929, states that natural ventilation may be em-
ployed for the ventilation of storage sections where it is practical to
maintain open windows or other openings at all times. The code specifies
that such openings shall be distributed as uniformly as possible in at least
two outside walls, and that the total area of such openings shall be
equivalent to at least 5 per cent of the floor area. The code further states
that where it is impractical to operate such a system of natural ventilation,
a mechanical system shall be used which shall provide for either the supply
of 1 cu ft of air per minute from out-of-doors for each square foot of floor
area, or for removing the same amount and discharging it to the outside
as a means of flushing the garage.
Research
Research on garage ventilation undertaken by the A.S.H.V.E. Com-
mittee on Research at Washington University, St. Louis, Mo., and at the
*Code for Heating and Ventilating Garages (A.S.H.V.E. TRANSACTIONS, Vol. 35, 1929).
Airation Study of Garages, by W. C. Randall and L. W. Leonhard (A.S.H.V.E. TRANSACTIONS, Vol. 36,
1930).
6Carbon Monoxide Concentration in Garages, by A. S. Langsdorf and R. R, Tucker (A.S.H.V.E. TRANS-
ACTIONS, Vol. 36, 1930).
Carbon Monoxide Distribution in Relation to the Ventilation of an Underground Ramp Garage, by
F. C. Houghten and Paul McDermott (A.S.H.V.E. TRANSACTIONS, Vol. 38, 1932).
Carbon Monoxide Distribution in Relation to the Ventilation of a One-Floor Garage, by F. C. Houghten
and Paul McDermott (A.S.H.V.E. TRANSACTIONS, Vol. 38, 1932).
Carbon Monoxide Distribution in Relation to the Heating and Ventilation of a One-Floor Garage, by
F. C. Houghten and Paul McDermott (A.S.H.V.E. Journal Section, Healing, Piping and Air Conditioning,
July, 1933).
Carbon Monoxide Surveys of Two Garages, by A. H. Sluss, E. K. Campbell and Louis M. Farber
(A.S.H.V.E. Journal Section, Heating, Piling and Air Conditioning, December, 1933).
CHAPTER 4 — -NATURAL VENTILATION
University of Kansas, Lawrence, Kans., in cooperation with the A.S.H.
V.E. Research Laboratory, and at the A.S.H.V.E. Research Laboratory
has resulted in authoritative papers on the subject.
Some of the conclusions from work at the Laboratory are listed below :
1. Upward ventilation results in a lower concentration of carbon monoxide at the
breathing line and a lower temperature above the breathing line than does downward
ventilation, for the same rate of carbon monoxide production, air change and the same
temperature at the 30-in. level.
2. A lower rate of air change and a smaller heating load are required with upward
than with downward ventilation.
3. In the average case upward ventilation results in a lower concentration of carbon
monoxide in the occupied portion of a garage than is had with complete mixing of the
exhaust gases and the air supplied. However, the variations in concentration from
point to point, together with the possible failure of the advantages of upward ventilation
to accrue, suggest the basing of garage ventilation on complete mixing and an air change
sufficient to dilute the exhaust gases to the allowable concentration of carbon monoxide.
4. The rate of carbon monoxide production by an idling car is shown to vary from
25 to 50 cfh, with an average rate of 35 cfh.
5. An air change of 350,000 cfh per idling car is required to keep the carbon monoxide
concentration down to one part in 10,000 parts of air.
PROBLEMS IN PRACTICE
1 • a. What means are available for the ventilation of buildings?
b. What precaution is necessary in combining different means of venti-
lating?
a. Natural forces, such as winds and stack effect, and mechanical forces furnished
by fans.
b. It is desirable that the different forces used be not in opposition. Their actions should
be mutually helpful. For example, a simple roof opening should be placed in the region
of lowest pressure caused by a prevailing wind. (See Fig. 1.)
2 • a. What factors are important in the location and control of ventilating
openings?
b. What types of ventilating openings are best suited to a proper distribu-
tion of the air supplied?
a. The proper distribution of air as required by the occupants, and the best utilization
of natural ventilating forces. The general rules on page 85 apply particularly to these
factors.
b. Windows with swinging sash and openings with deflectors may be used to direct air
to the points desired.
3 • a. What is the best location for ventilating openings?
b. How are the sizes of ventilating openings determined for proper air
supply?
a. Inlet openings should be low and facing the prevailing winds where possible. Outlet
openings should be high and on the side opposite the prevailing winds.
b. For simple openings use Formula 1:
Q = EAV
and for stacks use Formula 2:
Q = 9.4 A V H (ti - fe)
The use of these formulae is illustrated in Example 1 of the text of this chapter. Inlet
and outlet areas should be approximately the same for best results.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
4 • a. What are the advantages of roof ventilators?
h. How are proper sizes determined for roof ventilators?
a. Roof ventilators offer the best utilization of the inductive force of the wind, and they
may be very economically fitted with built-in fans to supply the necessary circulation
when the force of the wind is not sufficient.
b. Because of the many factors affecting the flow through roof ventilators no accurate
formula can be given. It is usual practice to make the combined throat area of all
roof ventilators between one-half area and full area of the air inlets as determined by
Formula 1.
5 • What methods of control are used in ventilating systems?
Hand control, control by a thermostat located in the ventilated space or in the venti-
lator, or wind velocity control designed to keep the air discharge constant regardless
of wind velocity.
6 • How is the quantity of air required for a huilding determined?
Sufficient air must be supplied to carry away the heat and impurities generated within a
building. The temperature rise and concentration of impurities in the exhaust air must
be held within specified limits. (See Example 1.)
7 • What measurements are necessary to determine the capacity of a venti-
lating system?
Wind velocity and air velocities through openings, determined by suitable cup anemo-
meters; outdoor air temperatures, measured by a shaded thermometer not near objects
heated by the sun or near exhaust air openings; indoor air temperatures, measured at
various heights to secure a good average.
8 • How much air must he supplied for dissipating the heat generated in a
dairy harn housing 100 cows if the outside temperature is 20 F and the inside
temperature is to be maintained at 45 F?
The total heat generated is 100 X 3000 = 300,000 Btu per hour or 5,000 Btu per
minute. Then from Formula 3,
o-HV
Q ~ CD
5000 X 13.5
"~ 0.24 X (45 - 20)
= 11,250 cu ft per minute.
This amount of air should also keep down humidity and odors.
9 • a. What precaution is necessary in the ventilation of garages using natural
ventilation?
h. How much window area is required for a garage with 50 x 100 sq ft floor
area if natural ventilation is used?
a. The carbon monoxide content of the air should be kept below 1 part in 10,000 and
windows should be kept open at all times.
b. The window area should aggregate 5 per cent of the floor area.
0.05 X 50 X 100 = 250 sq ft of window area.
This area should be evenly distributed along two sides of the building.
90
Chapter 5
HEAT TRANSMISSION COEFFICIENTS
AND TABLES
Heat Transfer, Calculations for Transmission Losses, Areas
Where Transmission Losses Occur, Coefficients of Transmission,
Table of Conductivities and Conductances, Tables of Over-all
Coefficients of Heat Transfer for Typical Building Constructions
*~r\O maintain specified inside temperature conditions and determine
JL the type of plant required, it is essential to know the transmission
losses of a structure and consider them in conjunction with the infiltration
losses.
Whenever a difference in temperature exists between the two sides of
any structural material, such as a wall or roof of a building, a transfer of
heat takes place through that material. When the inside temperature is
the higher, heat reaches or enters the inside surface of the wall by radia-
tion and convection, because the air and objects within the building are
always warmer than the inside surface of the wall when the inside air
temperature t is greater than the outside air temperature fe. This heat
must then pass through the material of the wall from the inside to the
outside surface by conduction, and is finally given off from the outside
surface by radiation and convection, provided, of course, that equilibrium
has been established and all four temperatures are constant. If the out-
side temperature is the higher, the reverse process takes place.
CALCULATIONS FOR TRANSMISSION LOSSES
The calculations for heat transmission losses are made by multiplying
the area A in square feet of wall, glass, roof, floor, or material through
which the loss takes place, by the proper coefficient U for such construc-
tion or material and by the temperature difference between the inside air
temperature t at the proper level (in many cases not the breathing-line)
and the outside air temperature t0. Therefore,
fit = A U (t - O (1)
where
Ht = Btu per hour transmitted through the material of the wall, glass, roof or
floor.
A a* area in square feet of wall, glass, roof, floor, or material, taken from building
plans or actually measured. (Use the net inside or heated surface dimensions
in all cases.)
t — t0 = temperature difference between inside and outside air, in which t must always
be taken at the proper level. Note that t may not be the breathing-line
temperature in all cases*
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Heat is lost from a building by transmission through all of those sur-
faces which separate heated spaces from the outside air or from unheated
colder spaces within the building. In general, five kinds of surfaces are
involved: (1) outside walls; (2) outside glass; (3) inside walls or parti-
tions next to unheated spaces; (4) ceilings of upper floors, either below a
cold attic space or as the underside of a roof slab ; and (5) floors of heated
rooms above an unheated space.
The net inside wall surface is usually determined by reference to the
scale plans and elevations of the building concerned. In some cases, of
course, the actual building may have to be measured. The total area of
all outside openings which are occupied by windows and doors is accurately
measured and listed as glass. The glass area is then deducted from the
total outside wall area for each room and the difference is the net wall
area. If there are no partitions, measure from the inside face of one wall
to the inside face of the next wall. The areas of walls, ceilings and floors
next to cold or unheated spaces are found, of course, by taking the inside
dimensions of such areas, measured on the heated side.
COEFFICIENTS OF TRANSMISSION
The coefficients of transmission may be determined by means of the
guarded hot box or the Nicholls heat meter described in Chapter 40, or
they may be calculated from fundamental constants. Because of the
unlimited number of combinations of building materials, it would be
impractical to attempt to determine by test the heat transmission co-
efficient of every type of construction in use; consequently, in most cases
it is advisable to calculate these coefficients.
Symbols
The following symbols are used in the heat transmission formulae in
this chapter:
U — thermal transmittance or over-all coefficient of heat transmission ; the amount of
heat expressed in Btu transmitted in one hour per square foot of the wall, floor, roof or
ceiling for a difference in temperature of 1 deg F between the air on the inside and that
on the outside of the wall, floor, roof or ceiling.
k = thermal conductivity; the amount of heat expressed in Btu transmitted in one
hour through 1 sq ft of a homogeneous material 1 in. thick for a difference in temperature
of 1 deg F between the two surfaces of the material. The conductivity of any material
depends on the structure of the material and its density. Heavy or dense materials, the
weight of which per cubic foot is high, usually transmit more heat than light or less dense
materials, the weight of which per cubic foot is low.
Ca = thermal conductance per unit area; the amount of heat expressed in Btu trans-
mitted in one hour through 1 sq ft of a non-homogeneous material for the thickness or
type under consideration for a difference in temperature of 1 deg F between the two
surfaces of the material. Conductance is usually used to designate the heat transmitted
through such heterogeneous materials as plaster board and hollow clay tile.
f — film or surface conductance; the amount of heat expressed in Btu transmitted by
radiation, conduction and convection from a surface to the air surrounding it, or vice
versa, in one hour per square foot of the surface for a difference in temperature of 1 deg F
between the surface and the surrounding air. To differentiate between inside and outside
wall (or floor, roof or ceiling) surfaces, /i is used to designate the inside film or surface
conductance and /0 the outside film or surface conductance.
a = thermal conductance of an air space; the amount of heat expressed in Btu trans-
mitted by radiation, conduction and convection in one hour through an area of 1 sq ft of
92
CHAPTER 5 — HEAT TRANSMISSION COEFFICIENTS AND TABLES
an air space for a temperature difference of 1 deg F. The conductance of an air space
depends on the mean absolute temperature, the width, the position and the character of
the materials enclosing it.
R = resjstance or resistivity which is the reciprocal of transmission, conductance,
or conductivity, i.e.:
— — = over-all or air-to-air resistance.
—j- = internal resistivity.
K
-~- ~ internal resistance.
C-a
-7- — film or surface resistance.
— = air-space resistance.
Fundamental Formulae
The formula of the over-all coefficient for a simple wall x inches thick is:
1
U
J_ + JL j_ _L
A k + /0
and for a compound wall of several materials having thicknesses in inches
of rci, #a, x3, etc., the coefficient is:
U
In the case of air-space construction, an air-space coefficient for each
air space must be inserted in either Equation 2 or 3. Thus for a simple
wall with one air space,
U
/0
and for a simple wall of several air spaces having conductances of
a*, a», etc., the coefficient is:
U
With certain special forms of materials which have irregular air spaces
(such as hollow tile) or are otherwise non-homogeneous, it is necessary
to use the conductance (Ca) for the unit construction, in which case
-r- is replaced by -~-.
As in the case of the simple wall, /i and /0 are always the inside and
outside surface coefficients for the two materials in contact with air. If
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
the air is still (no wind), then for the same material f\ and/0 are the same,
and/i = /0; but if the outside air is in motion, then/0 is always greater
than /i and will increase as the wind velocity increases. Values for fi in
still and moving air have been determined for various building materials
at the University of Minnesota under a cooperative research agreement
with the Society1. The range of values for ordinary building materials is
comparatively small and for practical purposes may be assumed constant
for either still air or any given wind velocity, particularly in view of the
fact that the surface resistances usually comprise only a small part of the
total resistance of the construction, except in the case of thin, highly
conductive walls. In determining basic heat transmission values for
building construction, it is customary to use that value of /0 which will
occur when a 15-mph wind blows parallel to the outer surfaces considered.
TABLE 1. CONDUCTANCES OF AIR SPACES a AT VARIOUS MEAN TEMPERATURES
MEAN
TUMP
DBO FAHK
CONDUCTANCES OF AIR SPACES FOR VARIOUS WIDTHS IN INCHES
0.128
0.250
0.364
0.493
0.713
1.00
1.500
20
2.300
1.370
1.180
1.100
1.040
1.030
1.022
30
2.385
1.425
1.234
1.148
1.080
1.070
1.065
40
2.470
1.480
1.288
1.193
1.125
1.112
1.105
50
2.560
1.535
1.340
1.242
1.168
1.152
1.149
60
2.650
1.590
1.390
1.295
1.210
1.195
1.188
70
2.730
1.648
1.440
1.340
1.250
1.240
1.228
80
2.819
1.702
1.492
1.390
1.295
1.280
1.270
90
2.908
1.757
1.547
1.433
1.340
1.320
1.310
100
2.990
1.813
1.600
1.486
1.380
1.362
1.350
110
3.078
1.870
1.650
1.534
1.425
1.402
1.392
120
3.167
1.928
1.700
1.580
1.467
1.445
1.435
130
3.250
1.980
1.750
1.630
1.510
1.485
1.475
140
3.340
2.035
1.800
1.680
1.550
1.530
1.519
150
3.425
2.090
1.852
1.728
1.592
1.569
1.559
aThermal Resistance of Air Spaces, by F. B. Rowley and A. B. Algren (A.S.H.V.E. TRANSACTIONS,
Vol. 35, 1929).
The conductances of air spaces at various mean temperatures and
widths, for ordinary building materials, are given in Table 1. These
results were likewise obtained at the University of Minnesota under a co-
operative research agreement with the Society.
Values for k and Ca, the conductivity and conductance of building ma-
terials and insulations, are given in Table 2 as taken from the published
values of various investigators. It should be noted that values of -k and
Ca as well as of U are dependent on the mean temperature, and it is
therefore desirable that the investigator determine heat-transmission
values under conditions approximating those existing under actual con-
ditions. Recommended values for calculating the coefficients of trans-
mission of various types of construction are marked by an asterisk in
Table 2.
^Surface Conductances as Affected by Air Velocity, Temperature and Character of Surface, by F. B.
Rowley, A. B. Algren and J. L. Blackshaw (A.S.H.V.E. TRANSACTIONS, Vol. 36, 1930). See also references
at end of chapter.
94
CHAPTER 5 — HEAT TRANSMISSION COEFFICIENTS AND TABLES
TABLE 2. CONDUCTIVITIES (k) AND CONDUCTANCES (Ca) OF BUILDING
MATERIALS AND INSULATORS^
7V«r coefficients are expressed in Btu per hour per square foot per degree Fahrenheit per 1 in. thickness,
•unless otherwise indicated.
I
Material
Description
DENSITY
(Le PER Cu FT)
If
M
CONDUCTIVITY (fc)
OR
CONDUCTANCE (Ca)
CIS 8
1s!
3 3
AUTHORITY
MASONRY MATERIALS
Common
5.00*
0.20
-
Face
9.20*
0.11
BRICKWORK.
Damp or wet._
5.00fr
0.20
(2)
Typical.
12.00*
0.08
UEMENT MO T _
Typical ....
110.0
75
5.20*
0.19
(3)
f(^ fl ,-Ttrge
Typical (8 in.)
0.62f*
1.61
UINDBE Dlt
u (12 in j" .
„
0.511*
1.96
CONCRETE
Typical -
12.00*>
0.08
1-2-4 mix. -
Various ages and mixesd
Cellular - -
143.0
40.0
69
75
9.46
11.35*0
16.36
1.06
0.11
0.94
(4)
(5)
(3)
50.0
75
1.44
0.69
(3)
a.
60 0
75
1.80
0.56
(3)
a
70.0
75
2.18
0.46
(3)
Typical gypsum fiber concrete, 87.5%
gypsum and 12 5% "wood chips
51.2
74
1.66*
0.60
(4)
CONCRETE BLOCKS
Special concrete made with an aggregate
of hardened clay — 1-2-3 mix. „
Typical (8 in )
101.0
70
3.98
l.OOf*
0.25
1.00
(3)
"" (12 in)
0.80f*
1.25
Special concrete block made with an aggre-
gate of hardened clay — 4 x 8 x 16 in.,
3 cores 18% voids
74 0
0.66f
1.51 -
(X\
Special concrete block made with an aggre-
gate of hardened clay— 8 x 8 x 16 in.,
4 cores 35% voids
74.5
0.30f
3.33
(3)
n
Typical
12.50*
0.08
STUCCO
12.00*
0.08
TILE
Typical hollow clay (4 in.)
i.oot*
1.00
(6 in.)"
0.64t*
1.57
-
(8 in )«
0.60J*
1.67
(10 in )e
0,58t*
K72
(1? in y
0.40f*
2.50
(16 in)'
0.31t*
3.23
•
Hollow clay (2 in.) M-in. plaster both sides
Hollow clay (4 in.) H-in. plaster both sides
Hollow clay (6 in.) ^in. plaster both sides
Hollow gypsum (4 in.)
120.0
127.0
124.3
110
100
105
l.OOf
0.60f
0.47f
0.46f
1.00
1.67
2.13
2.18
(2)
2)
(2)
51.8
70
1.66
0.60
(4)
Solid gypsum
75.6
76
2.96
0.34
<±)
TlLE OR. TBRRA.Z7O
Typical flooring
12.00*
0.08
,
AUTHORITIES:
1U. S. Bureau of Standards, tests based on samples submitted by manufacturers.
2A. C. Willard, L. C. Lichty, and L. A, Harding, tests conducted at the University of Illinois.
*J. C. Peebles, tests conducted at Armour Institute of Technology, based on samples submitted by manufacturers.
<F. B. Rowley, tests conducted at the University of Minnesota.
*A.S.H.V.E. Research Laboratory.
6K A. AUcut, tests conducted at the University of Toronto.
''Lees and Chorlton.
*Recommended conductivities and conductances far computing heat transmission coefficients.
tFor thickness stated or used on construction, not per 1-in. thickness.
*For additional conductivity data see Table 14, Page 63, 19$4 A..S.R.E. Data, Book.
^Recommended value. See Heating, Ventilating and Air Conditioning, by Harding and Willard, revised edition, 1932.
"One air cell in the direction of heat flow,
<*See A»SJB[.VJE. Research Paper, Conductivity of Concrete, by F. C. Houghten and Carl Gutberlet (A.S.H. V.E, TRANS-
ACTIONS, VoL 37, 1931).
<The 6-in,, 8-in., and 10-in, hollow tile figures are based on two cells in the direction of heat flow. The 124n. hollow tile
is based on three cells in the direction of heat flow. The 164n. hollow tile consists of one 10-in, and one 6-m. tile, each having
two cells in the direction of heat flow.
-'Not oompressed.
Hoofing, 0,15-in. thick (1.34 Ib per sq ft), covered witk gravel (0>83 ib per so; ft), combined thickness assumed 0.25.
95
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 2.
CONDUCTIVITIES (k) AND CONDUCTANCES (Ca) OF BUILDING
MATERIALS AND INSULATORS — Continued
The coefficients are expressed in Btu per hour per square foot per degree Fahrenheit per 1 in, thickness,
unless otherwise indicated.
Material
i
Description
DENSITY
(La PER Cu FT)
MEAN TEMP.
(DBQ FAHR)
CONDUCTIVITY (k)
OR
CONDUCTANCE (Ca)
ci^g
!1
S
o
<!
3)
1)
1)
1)
3)
1)
(1)
CD
(3)
1)
1)
1)
1)
3)
1)
3)
@
S
(3)
3)
1)
;i
8
1)
3)
ai
(i)
1
3)
1)
(1)
8
i)
i)
i)
(3)
(3)
INSULATION— BLANKET
OR FLEXIBLE TYPES
FIBER...- , „
Typical „_ _..
Chemically treated wood fibers held between
layers of strong paper/
Eel grass between strong paper /_„ „...
Flax fibers between strong paper/ _„
Hair felt between layers of paper/
Kapok between burlap or paper/.
3.62
4.60
3.40
4.90
11.00
1.00
70
90
90
90
75
90
0.27*
0.25
0.26
0.25
0.28
0.25
0.24
3.70
4.00
3.85
4.00
3.57
4.00
4.17
INSULATION-SEMI-
RIGID TYPE
Felted cattle hair/
13.00
11.00
12.10
13.60
7.80
6.30
6.10
6.70
10.00
11.00
90
90
70
90
90
90
90
75
90
70
0.26
0.26
0.30
0.32
0.28
0.27
0.26
0.25
0.37
0.26
3.84
3.84
3.33
3.12
3.57
3.70
3.85
4.00
2.70
3.84
Flax/
Flax and rye/
Felted hair and" asbestos/ „„
75% hair and 25% jute/
50% hair and 50% jute/
Jute/
Felted jute and asbestos/
Compressed peat moss
INSULATION— LOOSE
FILL OR BAT TYPE
Made from ceiba fibers/ , .
1.90
1.60
1.50
9.40
1.50
4.20
30.00
24.00
18.00
12.00
34.00
26.00
24.00
19.80
18.00
T.TO
21.00
18.00
14.00
10.00
14.50
14.50
11.50
75
75
75
103
75
72
90
90
90
90
90
90
75
90
75
90
90
90
90
90
77
75
72
86
.36
0.23
0.24
0.27
0.27
0.27
0.24
1.00
0.77
0.59
0.44
0.60
0.52
0.48*
0.35
0.34
0.27*
0.31
0.30
0.29
0.28
0.27*
0.33
0.38
0.31
1.04
0.71
4.35
4.17
3.70
3.70
3.70
4.17
1.00
1.30
1.69
2.27
1.67
1.92
2.08
2.86
2.94
3.70
3.22
3.33
3.45
3.57
3.70
3.03
2.63
3.22
0.96
1.41
GLASS WOOL.
Fibrous material made from dolomite and
silina. r ._-, 1L. n
Fibrous material made frnm slag, „,
Fibrous material 25 to 30 microns in dia-
meter, made from virgin bottle glass
Made from combined silicate of lime and
{ihltninf*- , .-.,L,-r r- ,r . ,L , lr ,,
GEANTJLAR_
N
GYPSUM, , „,
MINERAL WOOL™. ,~.
RKGRANTTI.ATEI> CORK
Cellular, dry
« a ~ *
Flaked, dry and fluffy/
« « « «
U it tt «
All forms, typical
About 2is-in. particles
ROCK WOOL
Fibrous material made from rock
« u « « u
Rock wool with a binding agent
Rock wool with flax, straw pulp, and binder
Rock wool with vegetable fibers _.
SAWDUST - .
Ordinary^ . „ „ . ...
SHAVINGS
Ordinary-
INSULATION-RIGID
CORKBOAED
Typical—
0.30*
0.34
0.30
0.27
0.25
0.32
0.33*
0.36
0,38
3.33
2.94
3.33
3.70
4.00
3.12
3.03
2.78
2.63
FIBER. . . . J
No added binder .,
« « u.
14.00
10.60
7.00
5.40
14.50
20.00
25.00
90
90
90
90
90
70
75
u. tt tt
« « a.
Asphaltic binder ,
Typical ,
Made from chemically treated wood fiber
Made from chemically treated wood and
vegetable fibers ,. ^ ... „
For notes see Page 95.
96
CHAPTER 5 — HEAT TRANSMISSION COEFFICIENTS AND TABLES
TABLE 2. CONDUCTIVITIES (k) AND CONDUCTANCES (Ca) OF BUILDING
MATERIALS AND INSULATORS — Continued
The coefficients are expressed in Btu per hour per square foot per degree Fahrenheit per 1 in. thickness,
unless otherwise indicated.
Material
Description
DENSITY
(Lu PER Cu FT)
MEAN TEMP.
(DEO FAHR)
CONDUCTIVITY (k)
OR
CONDUCTANCE (C )
^B
£Sfj
M g
« £
-<
INSULATION— RIGID
— Continued
FIBER
Made from corn stalks -
15.00
71
0.33
3 03
M)
" u exploded wood fiber
" " hard wood fibers
Insulating plaster 9/10-in. thick applied to
%-in. plaster board base
Made from licorice roots.,
Made from 85% magnesia and 15% asbestos
Made from shredded wood and cement
* " sugar cane fiber-
17.90
15.20
54.00
16.10
19.30
24.20
13.50
78
70
75
81
86
72
70
0.32
0.32
1.07f
0.34
0.51
0.46
0.33
3.12
3.12
0.93
2.94
1.96
2.17
3.03
(4)
(3)
(3)
(3)
(1)
(3)
H)
Sugar cane fiber insulation blocks encased in
asphalt membrane
Made from wheat straw _ _ ~
" wood fiber~—
13.80
17.00
15.90
15.00
70
68
72
70
0-30
0.33
0.33
0.33
3.33
3.03
3.03
3.03
(3)
(3)
3)
31
uu « _....
T.s"o
15.20
52
72
0.33
0.29
0.33
3.03
3.45
3.03
6)
3)
nt
* _
16.90
90
0.34
2.94
(i)
BUILDING BOARDS
ASBESTOS— — -
Compressed cement and asbestos sheets
Corrugated asbestos board ... _ „
123.00
20.40
86
110
2.70
0.48
0.37
2.08
(i)
(?)
GTPSTTML
Pressed asbestos mill board
Sheet asbestos
Gypsum between layers of heavy paper
60.50
48.30
62 80
86
110
70
0.84
0.29
1.41
1.19
3.45
0 71
CD
(2)
H)
PLASTER BOARD
Rigid, gypsum between layers of heavy
paper (J4-in. thick)
Gypsum mixed with sawdust between layers
of heavy paper (0.39-in. thick)
(3*3 "L)-- , . .
53.50
60.70
90
90
2.60f
3.60f
3.73J*
0.38
0.28
0.27
(1)
CD
(lx£ m>j
_..
2.82f*
0.35
_..
ROOFING CONSTRUCTION
ROOFING
Asphalt, composition or prepared
70.00
75
6.50P
0.15
m
SHINGLES. .„ _
Biult up — %-in. thick
Built up, bitumen and felt, gravel or slag
surfaced" „
Plaster board, gypsum fiber concrete and
3-ply roof covering, _
Agbftstos
52.40
65.00
76
75
3.53f*
1.33t
0.581
6-OOf*
0.28
0.75
1.72
0.17
(2)
(4)
(3)
Asphalt,
70.00
75
6.50J*
0.15
f3)
Sla'te
Wood
201.00
10.37*
1.28f
0.10
0.78
(7)
PLASTERING MATERIALS
PxAB-rmB.-™.^
CJfimfint , - ,
8.00
0.13
(2)
Gypsum, typical ,
Thickness % in
73
3.30*
8.80t
0.30
0.11
(T)
METAL LATH AND PLASTER
WOOD LATH AND PLASTER
Total thickness % in
H-ifc- plaster, total thickness % in — .
70
4.40f*
2.50J*
0.23
0.40
(4)
BUILDING
CONSTRUCTIONS
FRAME _
1-in. fir sheathing and building paper_
1-in. fir sheathing, building paper, and
yellow pine lap aiding., ^ , „. ^ _.
,
30
20
0.71t*
o.sot*
1.41
2.00
(4)
(4)
FLOORING
1-in. fir sheathing, building paper and stucco
Pine lap siding and building paper — aiding
4 in. wide
Yellow pine lap siding
Maple — across grain
40".00
20
16
75
0.82f*
0.85f*
1.28f*
1.20
1,22
1.18
0.78
0.83
(4)
(4)
(7)
Battleship linoleum CJ^~i^ )
1.36f*
0.74
For notes see Page 95.
97
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 2. CONDUCTIVITIES (k) AND CONDUCTANCES (Ca) OF BUILDING
MATERIALS AND INSULATORS — Continued
The coefficients are expressed in Btu per hour per square foot per degree Fahrenheit per 1 in. thickness,
unless otherwise indicated.
J
Material
Description
DENSITY
(Ln PER Cu FT)
1
CONDUCTIVITT (k)
OH
CONDUCTANCE (Ca)
3s
§ i
<§ s
AUTHORITY
AIR SPACE AND SURFACE
COEFFICIENTS
Am ppA.rRp
• • • • •
Over %-in, faced with ordinary building
materials •- -
40
not*
0.91
(4)
_ ~
Still air (/i) . -
1.65f*
0.61
(4)
SURFACES,
IS mph — (/o)
6.00f*
0.17
(4)
j, Tj . ,
Still air (/i)
60
i.iat
0.85
AIR SPACESTACED WITH
BRIGHT ALUMINUM
FOIL
Air space, faced one side with, bright alumi-
num foil, over iNt-in. wide .. ...
Air space, faced one side with bright alumi-
num foil, 5£-in. wide . -
Air space, faced both sides with bright
aluminum foil over 3^-in. wide
50
50
50
0.46f*
0.62t
0.41 f*
2.17
1.61
2.44
(4)
(4)
(4)
Air space, faced both" sides with bright
j\IiiTTunum foil 5^-in 'widft
50
O.S7f
1.75
(4)
Air space divided 'in two with single curtain
of bright aluminum foil (both sides bright)
Each space over /^-in. wide -
50
0.23f*
4.35
(4)
Each space i^-in. wide . .~ . .
Air space with multiple curtains of bright
aluminum foil, bright on both sides,
curtains more than %-in. apart, in
standard construction
2 curtains forming 3 spaces
50
50
O.Slf
O.lSf*
3.23
6.67
(4)
(4)
3 curtains forming 4 spjujss
50
O.llf*
9.09
(4)
4 curtains forming 5 spaces
50
0.09t*
11.11
(4)
WOODS (Across Grain)
BALSA
20.0
90
0.58
1.72
(1)
8.8
90
0.38
2.63
1)
7.3
90
0.33
3.03
1)
CALIPORNTA^Tl'BTyWOOr*
0% moisture -
22.0
75
0.66
1.53
4)
Q% u
28.0
75
0.70
1.43
4)
8% «
22.0
75
0.70
1.43
4)
8% "
28.0
75
0.75
1.33
4)
16% u
22.0
75
0.74
1.35
4)
16% «
28.0
75
0.80
1.25
(4)
CYPBBSP
28.7
86
0.67
1.49
(1)
0% moisture
26.0
75
0.61
1.64
(4)
1 . . n,,..^
0% u
34 0
75
0.67
1.49
f4)
8% "
26.0
75
0.66
1.52
(4)
8% "
34.0
75
0.75
1.33
(4)
169' "
26.0
75
0.76
1.32
4)
16^ u
34.0
75
0.82
1.22
4)
EASTERN HEMLOCK
0% moisture .
22.0
75
0.60
1.67
4)
30.0
75
0.76
1.32
4}
gm «
22.0
75
0.63
1.59
4)
^1 ; -
30.0
22.0
75
75
0.81
0.67
1.23
1.49
(4)
(4)
16% "
30.0
75
0.85
1.18
(4)
HARD MAPLE '
0% moisture
40.0
75
1.01
0.99
(4)
"iv""-"*— """ " "*
46.0
75
1.05
0.95
4)
gw «
40.0
75
1.08
0.93
4)
om «
46.0
75
1.13
0.89
4)
16*7 *
40.0
75
1.15
0.87
4)'
16% "
46.0
75
1.21
0.83
4)
For notes see Page 95.
CHAPTER 5 — HEAT TRANSMISSION COEFFICIENTS AND TABLES
TABLE 2. CONDUCTIVITIES (k) AND CONDUCTANCES (Ca) OF BUILDING
MATERIALS AND INSULATORS — Continued
The ccejfir.ients are expressed in Btu per hour per square foot per degree Fahrenheit per 1 in. thickness,
unless other-wise indicated.
Material
Description
DENSITY
(La PER Cu FT)
MEAN TKMP.
(DEO FARE)
CONDUCTIVITY (k)
on
CONDUCTANCE (C&)
Is!
S &
AUTHOHITY
WOODS— Continued
LONGLEAF YELLOW PINE _
0% moisture
30.0
75
0.76
1.32
(4)
0%
40.0
75
0.86
1.16
(4)
8%
30.0
75
0.83
1.21
C4>
^%
40 0
75
0.95
1-05
M)
16%
30.0
75
0.89
1.12
(4)
l^ or
40.0
75
1.03
0.97
(4)
MAHOGANY
34.3
86
0.90
1.11
f1>
44 3
86
1 10
0.91
0)
\^APTi1?5 ^R OATC
1.15*
0.87
NORWAY PINE,™ r , , »T
§mm"ntnre
22.0
75
0.62
1.61
(4)
32.0
75
0.74
1.35
(4)
22.0
75
0.68
1.47
ffl
32.0
75-
0.83
1.21
(4)
•\ffi7
22.0
75
0.74
1.35
(4)
\(\°7
32.0
75
0.91
1.10
{4
RED CYPKBSS-
n°7 moisture
22.0
75
0.67
1.49
4
Qcr
32 0
75
0 79
1.27
4
gcr
22.0
75
0.71
1.41
4
8%
32.0
75
0.84
1.19
4
1^%
22.0
75
0.74
1.35
4)
1^%
32.0
75
0.90
1.11
4)
P,*m OAW
0% moisture
38.0
75
0.98
1.02
4)
48.0
75
1.18
0.85
4)
8%
38.0
75
1.03
0.97
4)
jjor
48.0
75
1.24
0.81
4)
•j^O/
38.0
75
1.07
0.94
4)
•Jri^
48.0
75
1.29
0.78
4)
SJHOSTT..TAV YfeL^OW PfNTB . .
O^7" Tpoi^ttire
26.0
75
0.74
1.35
4)
n^
36.0
75
0.91
1.10
4)
8%
26.0
75
0.79
1.27
4)
?%
36.0
75
0.97
1.03
(4
16%
26.0
75
0.84
1.19
(4
16%
36.0
75
1.04
0.96
SOFT Er,v
n% mois ure lr ,
28.0
75
0.73
1.37
(4
n%
34.0
75
0.88
1.14
4
28.0
75
0.77
.30
4
^ttr
34.0
75
0.93
.08
4
•j^ttr
28.0
75
0.81
.24
4
16%
34.0
75
0.97
.03
4
0% moisture
36.0
42.0
75
75
0.95
.05
4)
fftf
36.0
75
0.96
.04
4}
8%
42.0
75
1.02
.98
4)
169^
36.0
75
1.01
.99
4)
16%
42.0
75
1.09
.92
4>
SiftJAR PINE
0% mois rrrA „, ,
22.0
75
0.54
.85
28.0
75
0.64
.56
4
$Of
22.0
75
0.59
.70
4
9P7
28.0
75
0.71
.41
4
\fp?
22.0
75
0.65
.54
4
1^%
28.0
75
0.78
.28
4
VTWOTWTA, Pr^
34.3
86
0.96
1)
Www COAST HKMKK^
0% moisture... .L ^ ^ ,
22.0
75
0.68
.47
4>
0%
30.0
75
0.79
.27
4>
W?
22.0
75
0.73
.37
4>
%°7
30.0
75
0.85
.18
4)
\f\°7
22.0
75
0.78
.28
4>
\&
30.0
75
0.91
.10
4)
WBTTTB PjN^.rnirJ1 ._ „ _
'
31.2
86
0.78
.28
Yur.T.nw. Prism -,„,„,.
1.00
.00
D
YELLOW PINK OR "Prp JU-J
0.80*
1.25
For notes see Page 95.
99
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 3. COEFFICIENTS OF TRANSMISSION ( U) OF MASONRY WALLS<J
Coefficients are expressed in Btu per hour per square foot per degree
Fahrenheit difference in temperature between the air on the two sides,
and are based on a wind velocity of 15 mph.
THICKNESS
r
rYp
[CAL
OP
WALL
CONSTRUCTION
TYPE OF WALL
MASONRY
No.
(INCHES)
I
c
£
t
^
a
3C
•^»*,
53Sp>j
53
383
H^?
^
,/TUCCO\
SoUd Brick
Based on 4-in. face brick and the remainder
common brick.
B
12
16
1
2
3
—- *
^
m
SS=
y
Hollow Tile
T
^.
^tSr
^^
Stucco Exterior Finish.
The 8-in. and 10-in. tile figures are based on
8
4
two cells in the direction of flow of heat. The
10
- 5
12-in. tile is based on three cells in the direc-
12
6
tion of flow of heat. The 16-in. tile consists
16
7
Li
*+,
^^
*^^
^
of one 10-in. tile and one 6-in. tile each having
two cells in the direction of heat flow.
I
-=±:
t
^
— ^^.
^
0
&
S
tp.
K
T ^
&
12
9
: 1
%..
£*>?f
j
Limestone or Sandstone
16
10
1
1
-ji
•*-*^
\>
?
24
11
^
~* i.
Concrete
6
12
.. ',
w «
o.
» -
These figures may be used with sufficient
10
13
accuracy for concrete walls with stucco
16
14
-;'
o '
— il>
1^ .
£
exterior finish.
20
15
f=\
jg
g
g^
n
Hollow Cinder Blocks
S
16
Based on one air cell in direction of heat flow.
12
17
r
Hollow Concrete Blocks
B
IS
^
^
******
La,
•~.
t
53S
—».
^
/
I
Based on one air cell in direction of heat flow.
12
19
"Computed from factors marked by * in Table 2.
6 Based on the actual thickness of 2-in. furring strips.
100
CHAPTER 5 — HEAT TRANSMISSION COEFFICIENTS AND TABLES
INTERIOH FINISH
UNINSULATED WA.LLS
INSTTLA.TED WALLS
1
1
c
§
s
H
3 is
-1
||.l
ja
i
*
3
•f
1
S
2,3 ^
"cS g*O
li
1^
-s
"S
^
•S
T3
•*"
^7
5&01
J» 2
•£&"•!>.
in walla — no interior fir
ister (^ in.) on walls
«2
k
1
c
o
ister (% in.) on metal 1
•o,
J!i"
corated building boar
hout plaster — furred
5
•g
o
-2 S
a
o
&l
It
tflter (li in.) on corkboa
in cement mortar (l/i \
ster (% in.) on metal la
furring strips — furred i
in. wide) faced one
ght aluminum foil
15
§f|
ister (% in.) on metal la
furring strips (2 in.
ulation (*<£ m.) betwt
ipa (one sur space)
5
fi
s
g
pui
Q'S
E^
Sci
ei
SS^S
las
ssJ-g
A
B
c
D
E
F
G
H
i
J
K
L
0.50
0.46
0.30
0.32
0.30
0.23
0.22
0.16
0.14
0.23
0.12
0.20
0.36
0.34
0.24
0.25
0.24
0.19
0.19
0.14
0.12
0.19
0.11
0.17
0.28
0.27
0.20
0.21
0.20
0.17
0.16
0.13
0.11
0.17
0.10
0.15
0.40
0.39
0.37
0.37
0.26
0.26
0.27
0.27
0.26
0.26
0.20
0.20
0.20
0.19
0.15
0.15
0.13
0.13
0.20
0.20
0.11
0.11
0.18
0.18
0.30
0.29
0.22
0.22
0.22
0.17
0.17
0.13
0.12
0.17
0.10
0.16
0.25
0.24
0.19
0.19
0.19
0.15
0.15
0.12
0.11
0.15
0.097
0.14
0.71
0.64
0.37
0.39
0.37
0.26
0.25
0.18
0.15
0.26
0.13
0.23
0.58
0.53
0.33
0.34
0.33
0.24
0.23
0.17
0.14
0.24
0.13
0.21
0.49
0.45
0.30
0.31
0.30
0.22
0.22
0.16
0.14
0.22
0.12
0.20
0.37
0.35
0.25
0.26
0.25
0.20
0.19
0.15
0.13
0.20
0.11
0.18
0.79
0.70
0.39
0.42
0.39
0.27
0.26
0.19
0.16
0.27
0.13
0.23
0.62
0.57
0.34
0.37
0.34
0.25
0.24
0.18
0.15
0.25
0.13
0.22
0.48
0.44
0.29
0.31
0.29
0.22
0.21
0.16
0.14
0.22
0.12
0.20
0.41
0.39
0.27
0.28
0.27
0.21
0.20
0.15
0.13
0.21
0.12
0.18
0.42
0.39
0.27
0.28
0.27
0.21
0.20
0.16
0.13
0.21
0.12
0.19
0.37
0.35
0.25
0.26
0.25
0.19
0.19
0.15
0.13
0.19
0.11
0.17
0.56
0.52
0.32
0.34
0.32
0.24
0.23
0.17
0.14
0.24
0.12
0.21
0.49
0.46
0.30
0.32
0.30
0.23
0.22
0.16
0.14
0.23
0.12
0.20
«A waterproof membrane should be provided between the outer material and the insulation fill to
prevent possible wetting by absorption and a subsequent lowering of efficiency.
101
AMERICAN SOCIETY- of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TA.BLE 4. COEFFICIENTS OF TRANSMISSION (U) OF MASONRY WALLS
WITH VARIOUS TYPES OF VENEERS*
Coefficients are expressed in Btu -per hour per square foot per degree
Fahrenheit difference in temperature between the air on the two sides,
and are based on a wind velocity of 15 mph.
TYPICAL
CONSTRUCTION
TYPE OF WALL
FACING
BACKING
WALL
No.
4 in. Brick Veneer^
6 in.
Sin.
10 in.
12 in.
Hollow Tile*
4 in. Brick Veneer*
Gin.
10 in. Concrete
16 in.
4 in. Brick Veneer''
8 in.
12 in.
Cinder Blocks*
4 in. Brick Veneer''
Sin.
12 in.
Concrete Blocks*
4 in. Cut-Stone Veneer*
8 in.
12 in. Common Brick
16 in.
4 in. Cut-Stone Veneer<*
6 in.
10 in
12 in.
Hollow Tile-
4 in. Cut-Stone Veneerd
6 in,
10 in. Concrete
16 in.
20
21
22
23
24
25
26
27
28
29
30
31
32
33
34
35
36
37
38
39
40
flComputed from factors marked by * in Table 2.
6 Based on the actual thickness of 2-in, furring strips.
*The 6-fn., 8-in. and 10-in.,tile figures are based on two cells in the direction of heat flow. The 12-in.
tile is based on three cells in the direction of heat flow.
102
CHAPTER 5 — HEAT TRANSMISSION COEFFICIENTS AND TABLES
INTERIOR FINISH
UNINSULATED WALLS
INSULATED WALLS
f!
ii
g
g
c
•S|3
"81
•35 S
J.s
3
£
§
If*
3.2
111
JS,
"8
J,
3
S^
8
X
s
III
*"§
jjt fl
•1
g
J5
J
-0
S
X
q en
11
jlla 1
s
JS
'-•
T
-2
*•!
•c
•S1
"^ £; o
His'
Plain walls — no inter
Plaster (^ in.) on wa
§
Plaster (^ in.) on m
g
!f
-2 5
li
No plaster — decorate
ing board interior i
furred
a
o
^5
^1
&?
o
sl
I!
Plaster on corkboard
cement mortar (H in
Plaster on metal lath
to furring strips— fui
J£:in. wide) faced
bright aluminum foil
Plaster (% in.) on me
to furring strips (2 i
fill (1% in.b)/
Plaster (% in.) on me
to furring strips (
insulation (^ m.)
strips (one air space)
A
B
c
D
E
F
G
H
I
J
K
L
0.36
0.34
0.24
0.25
0.24
0.19
0.19
0.16
0.13
0.19
0.11
0.17
0.34
0.33
0.24
0.25
0.24
0.19
0.18
0.14
0.12
0.19
0.11
0.17
0.34
0.32
0.23
0.24
0.23
0.19
0.18
0.14
0.12
0.19
0.11
0.17
0.27
0.26
0.20
0.21
0.20
0.16
0.16
0.13
0.11
0.16
0.10
0.15
0.57
0.53
0.33
0.35
0.33
0.24
0.23
0.17
0.14
0.24
0.13
0.21
0.48
0.45
0.30
0.31
0.30
0.22
0.22
0.16
0.14
0.22
0.12
0.20
0.39
0.37
0.26
0.27
0.26
0.20
0.19
0.15
0.13
0.20
0.11
0.18
0.35
0.31
0.33
0.30
0.24
0.22
0.25
0.23
0.24
0.22
0.19
0.18
0.18
0.17
0.14
0.14
0.12
0.12
0.19
0.18
0.11
0.11
0.17
0.16
0.44
0.42
0.28
0.30
0.28
0.21
0.21
0.16
0.13
0.21
0.12
0.19
0.40
0.38
0.26
0.28
0.26
0.20
0.20
0.15
0.13
0.20
0.11
0.18
0.37
0.35
0.25
0.26
0.25
0.19
0.19
0.15
0.13
0.19
0.11
0.17
0.28
0.27
0.21
0.21
0.21
0.17
0.16
0.13
0.12
0.17
0.10
0.15
0.23
0.22
0.18
0.18
0.18
0.15
0.14
0.12
0.11
0.15
0.095
0.14
0.37
0.36
0.35
0.34
0.25
0.24
0.26
0.25
0.25
0.24
0.20
0.19
0.19
0.19
0.15
0.15
0.13
0.13
0.20
0.19
0.11
0.11
0.18
0.17
0.35
0.33
0.24
0.25
0.24
0.19
0.18
0.14
0.12
0.19
0.11
0.17
0.28
0.26
0.20
0.21
0.20
0.17
0.16
0.13
0.11
0.17
0.10
0.15
0.61
0.56
0.34
0.36
0.34
0.25
0.24
0.18
0.15
0.25
0.13
0.22
0.51
0.47
0.31
0.32
0.31
0.23
0.22
0.17
0.14
0.23
0.12
0.20
0.41
0.38
0.26
0.28
0.26
0.20
0.20
0.15
0.13
0.21
0.11
0.18
^Calculations include cement mortar (J^ in.) between veneer or facing and backing.
•Based on one air cell in direction of heat flow.
/A waterproof membrane should be provided between the outer material and the insulation fill to
prevent possible wetting by absorption and a subsequent lowering of efficiency.
103
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 5. COEFFICIENTS OF TRANSMISSION ( U) OF
VARIOUS TYPES OF FRAME CONSTRUCTION^
These coefficients are expressed in Bin per hour per square foot per
degree Fahrenheit difference in temperature between the air on the two
sides, and are based on a wind Telocity of 16 mph.
TYPICAL
CONSTRUCTION
EXTERIOR FINISH
TYPE OF SHEATHING
voop
1 in. Wood*
Wood Siding or Clapboard
in. Rigid Insulation
in. Plaster Board
W00.D
1 in. Wood*
Wood Shingles
in. Rigid Insulation*
in. Plaster Board*
1 in. Wood*
Stucco
in. Rigid Insulation
/HEAWNQ-
in. Plaster Board
1 in. Wood*
Brick/ Veneer
in. Rigid Insulation
in. Plaster Board
41
42
43
44
45
47
48
49
50
51
52
^Computed from factors marked by * in Table 2.
6These coefficients may alsoibe^used with sufficient accuracy for plaster on wood lath or plaster on
plaster board.
'Based on the actual width of 2 by 4 studding, namely, 3£i in.
104
CHAPTER 5 — HEAT TRANSMISSION COEFFICIENTS AND TABLES
INTERIOR FINISH
No INSULATION BETWEEN STUDDING
e
o
i
§
§
c
2
^i
0 c:
§35
bfl
5
.§
"5
"3
^x
.2
T!i
§^5
?
~
&
.§
S
^
°.s
1^
•^c
e^
1
0
i,
1
1
0
'.^S
±^
•|=3
l||
§
^
-S
3-1
fo
S
S-
al-5
c
o
° P?
S £#
5.2
0
rt«3
g
O § a
§— §
i
£2
31
31
2-5
g
-0_g
0 0
e£ rs
.?^|
jll
§
ts5
S|
si
^4
i!
!i
sr|
?l|f
t.2
•2.5
l'"-
JSB
-Is
|g|
SJS g
•^T| |^
1
— 5
— ^*
sS
5
5 §
I.S
sil
slS
liS-a
A
B
C
D
E
F
G
H
i
j
0.25
0.26
0.25
0.19
0.15
0.11
0.19
0.19
0.061
0.17
0.23
0.24
0.23
0.18
0.14
0.11
0.18
0.18
0.060
0.17
0.31
0.33
0.31
0.22
0.17
0.13
0.23
0.23
0.064
0.20
0.25
0.26
0.25
0.19
0.15
0.11
0.19
0.19
0.061
0.17
0.19
0.20
0.19
0.15
0.12
0.10
0.16
0.16
0.057
0.14
0.24
0.25
0.24
0.19
0.15
0.11
0.19
0.19
0.061
0.17
0.30
0.31
0.30
0.22
0.16
0.12
0.22
0.22
, 0.064
0.20
0.27
0.29
0.27
0.20
0.16
0.12
0.21
0.21
0.062
0.19
0.40
0.43
0.40
0.26
0.19
0.14
0.28
0.28
0.067
0.24
0.27
0.28
0.27
0.20
0.15
0.12
0.21
0.21
0.062
0.18
0.25
0.26
0.25
0.19
0.15
0.11
0.19
0.20
0.061
0.18
0.35
0.37
0.35
0.24
0.18
0.13
0.25
0.25
0.066
0.22
INSULATION BETWEEN STUDDING
<fY"eIIow' pine or fir — actual thickness about K/& in.
•Furring strips between wood shingles and sheathing.
•''Small air space and mortar between building paper and brick veneer neglected.
*A waterproof membrane should Tbe provided* between £he outer material and the insulation fill to
prevent possible wetting by absorption and a subsequent towering1 of efficiency. .
I05:
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 6. COEFFICIENTS OF TRANSMISSION (U) OF FRAME INTERIOR WALLS
AND PARTITIONS^
Coefficients are expressed in Btu Per hour per square foot per degree Fahrenheit difference in temperature
between the air on the two sides, and are based on still air (no 'wind) conditions on both sides.
TYPICAL
^LA/T
PU
CONSTRUCTION
ER, yTUK/
feSu
WALL
No.
SLVGLE
PARTITION
(FINISH
ON ONE
SIDE OP
STUDDING)
DOUBLE PARTITION
(FINISHED ON BOTH SIDES OP STUDDING)
Air
Space
Between
Studding
Flaked
Gypsum
Fill*
Between
Studding
Rock
Wool
Fill*
Between
Studding
l/z-in.
Flexible
Insulation
Between
Studding
(One Air
Space)
Stud Space Faced
One Side with
Bright Aluminum
Foil
TYPE OF WALL
A
B
C
D
E
F
Wood Lath and Plaster
On Studding
53
0.62
0.34
0.11
0.065
0.21
0.24
Metal Lath and Plaster*
On Studding
54
0.69
0.39
0.11
0.066
0.23
0.26
Plaster Board (% in.) and
Plaster** On Studding
55
0.61
0.34
0.10
0.065
0.21
0.24
$4 in. Rigid Insulation and
Plaster* On Studding
56
0.35
0.18
0.083
0.056
0.14
0.15
1 in. Rigid Insulation and
Plaster* On Studding
57
0.23
0.12
0.066
0.048
0.097
0.10
IK in- Corkboard and
Plaster* On Studding
58
0.16
0.081
0.052
0.040
0.070
0.073
2 in. Corkboard and
Plaster* On Studding
59
0.12
0.063
0.045
0.035
0.057
0.059
•Computed from factors marked by
^Thickness assumed 3jhf in.
* in Table 2. 'Plaster on metal lath assumed %-in. thick.
^Plaster assumed K-in. thick.
TABLE 7. COEFFICIENTS OF TRANSMISSION (U) OF MASONRY PARTITIONS*
Coefficients are expressed in Btu per hour Per square foot Per degree Fahrenheit difference in temperature
between the air on the two sides, and are based on still air (no wind) conditions on both sides.
TYPICAL CONSTRUCTION
1
Ste^*!
No.
PLAIN WALLS
(No PLASTER)
WALLS
PLASTERED
ON ONE SIDE
WALLS
PLASTERED
ON BOTH SIDES
|| .u.'""-
r/ : -.jig-.
TYPE OF WALL
A
B
C
4-in. Hollow Clay Tile
60
0.45
0.42
0.40
4-in. Common
Brick
61
0.50
0.46
0.43
4-in. Hollow Gypsum Tile
62
0.30
0.28
0.27
2-in. Solid Plaster
63
0.53
•Computed from factors marked by * in Table 2.
106
CHAPTER 5 — HEAT TRANSMISSION COEFFICIENTS AND TABLES
;
i ;
i
"S
•§el to
c
rt
.?JlgJI
«
CO
M
W
S3
co
r-t
T-*
S
O
0
IH
0
J
^^J *^J
o
0
0
0
O
O
o
o
0
O
o
"5
pqt-5 § fe
*o
w
rf
1 §.§1a
o
^*
*53
d
32
s.l?l|
fi
CO
iS
a;
S!
cc
i3
S
C5
g
^
§
1
e **
•^ o^f^ j.
o
o
o
0
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Coefficients are e:
i
5
u
§
i
-00
Lath and Plaster (££ in.
Lath and Plaster
i
1
i
h
[nsulation (}A in.) and PI
Lath and Plaster
Lath and Plaster
Lath and Plaster
Lath and Plaster
V
OB
£
•e
§
r-l
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oard (2 in.) and Plaster i
mputed from factors mark
ickness assumed to be *56 i
ckness assumed to be % i
sed on one air space with
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O
1
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1-
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107
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
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108
CHAPTER 5 — HEAT TRANSMISSION COEFFICIENTS AND TABLES
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'ABLE 10. COEFF
Coefficients are
TYPICAL CONSTETJi
COHCR.^^ /FLOi
YPB AND THICKNESS OP
Rigid Insulation6
Rigid Insulation6
Corkboard"
Corkboard*
Computed from facto;
ssumed % in. thick,
.ssumed *% in. thick.
Lssumed 1 in. thick,
'he figures for Nos. 5
concrete, Usually tl
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109
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 11. COEFFICIENTS OF TRANSMISSION (U) OF VARIOUS TYPES
OF FLAT ROOFS COVERED WITH BUILT-UP ROOFING*
TYPICAL CONSTRUCTION
1
1
i WITH METAL LATH
WITHOUT CEILINGS AND
PLASTEH CEILINGS*
TYPE OF ROOF DECK
THICKITOSS
OP
ROOF
DECK.
(INCHES)
No.
•t^sr /£*3T
XOOFlKCj /Tut ROOriNrfj /THE,
^jL:: -..-.•: • -. ^ • 3r] [?P f.-:- ••?-•--:,> «
Precast Cement Tile
1H
1
^/WPP^T/^ UfiTirj>ri'-
CtlUKfi'^
irVULAUON/ „ ^B1Ir'/oUTuw/
*OOMN<fc / F.oonft<s> /
Concrete
-2
2
f^'^H'^'il'ft ^••:fejd
Concrete
4
3
coMCRtTC.^ concntTE./ jiTj
Concrete
Q
4
^ElLlMd/
1N/ULA.TION/ ,e,li'iULAri('"/
lOOHNffj / ROOFlflffl /
Wood
Wood
1*
1 LjTfc
5
^
557J ) )T J V 7 j» >V /J Si ry/yy yyf y./.*
'«,«>' p|-»' g(
Wood
Wood
#*
4>
7
8
CLtlllHtf^.
iNJULtftOtt/ Itl/ULAtlfln/
RflflRHCi 7 T.«OPIM<^ ^
Gypsum Fiber Concrete6
(2 in ) on Plaster Board
f «f r/y n- :-. - : -V- j ^^ "^ * "" ?:*:'"''>]
(H in.)
2H
9
fLAJTCR. 50AfcP^ PUA/TCR. MAH.P*
Gypsum Fiber Concrete6
(3 in.) on Plaster Board
CttUWtf'^ '
(H in.)
3%
10
MOHruTi7 ^g^""(
Flat Metal Roofs
Coefficient of transmis-
sion of bare corrugated
<^]jjf'™^ |'E""?iPr;
Btu per hour per square
foot of projected area per
11
dElLTHd^
ference in temperature,
based on an outside wind
velocity of 15 mph.
°Computed from factors marked by * in Table 2.
^Nominal thicknesses specified — actual thicknesses used in calculations.
*Gypsum fiber concrete — 87K per cent gypsum, 12>£ per cent wood fiber.
110
CHAPTER 5 — HEAT TRANSMISSION COEFFICIENTS AND TABLES
Coefficients are expressed in Btu per hour per square foot per degree
Fahrenheit difference in temperature bet-ween the air on the two sides,
and are based on an outside wind velocity of 15 mph.
WITHOUT CEILING-UNDER SIDE OF
HOOF EXPOSED
WITH METAL LATH AND
PLASTER, CEILINGS*
c
3
i
c
c
S
a
a
s
.0
JS
i
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1
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1
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1
a
1
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5
a
t
|
6
i
o
a
1
A
B
c
D
E
F
G
H
I
T
K
L
M
N
0
P
0.84
0.37
0.24
0.18
0.14
0.22
0.16
0.13
0.43
0.26
0.19
0.15
0.12
0.18
0.14
0.11
0.82
0.72
0.64
0.37
0.34
0.33
0.24
0.23
0.22
0.17
0.17
0.16
0.14
0.13
0.13
0.22
0.21
0.21
0.16
0.16
0.15
0.13
0.12
0.12
0.42
0.40
0.37
0.26
0.25
0.24
0.19
0.18
0.18
0.15
0.14
0.14
0.12
0.12
0.11
0.18
0.17
0.17
0.14
0.13
0.13
0.11
0.11
0.11
0.49
0.37
0.32
0.23
0.28
0.24
0.22
0.17
0.20
0.18
0.16
0.14
0.15
0.14
0.13
0.11
0.12
0.11
0.11
0.096
0.19
0.17
0.16
0.13
0.14
0.13
0.12
0.11
0.12
0.11
0.10
0.091
0.32
0.26
0.24
0.18
0.21
0.19
0.17
0.14
0.16
0.15
0.14
0.12
0.13
0.12
0.11
0.10
0.11
0.10
0.097
0.087
0.15
0.14
0.13
0.11
0.12
0.11
0.11
0.096
0.10
0.095
0.092
0.082
0.40
0.25
0.18
0.14
0.12
0.17
0.13
0.11
0.27
0.19
0.15
0.12
0.10
0.14
0.12
0.097
0.32
0.22
0.16
0.13
0.11
0.15
0.12
0.10
0.23
0.17
0.14
0.11
0.097
0.13
0.11
0.091
0.95
0.39
0.25
0.18
0.14
0.23
0.17
0.13
0.46
0.27
0.19
0.15
0.12
0.18
0.14
0.11
*These coefficients may be used with sufficient accuracy for wood lath and plastert or plaster board and
plaster ceilings. It is assumed that there is an air space between the under side of the roof deck and the
upper side of the ceiling.
Ill
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
II
8 1
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to •§ £
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112
CHAPTER 5 — HEAT TRANSMISSION COEFFICIENTS AND TABLES
TABLE 13. COEFFICIENTS OF TRANSMISSION (Z7) OF DOORS, WINDOWS AND SKYLIGHTS
Coefficients are based on a wind velocity of 15 mph, and are expressed in Btu per hour per square foot per
degree Fahrenheit difference in temperature between the air inside and outside of the door, window or skylight
A. Windows and Skylights
U
Single
Double....
Triple
1.13*.*
0.45'
0.281*
B. Solid Wood Doors**
NOMINAL
THICKNESS
INCHES
ACTTTiL
THICKNESS
INCHES
17
1
%
0.69
1H
IHe
0.59
1H
We
0.52
IX
1H
0.51
2
1%
0.46
2H
2H
0.38
3
2^i
0.33
•See Heating, Ventilating and Air Conditioning, by Harding and Willard, revised edition, 1932.
*Computed using C = 1.15 for wood;/i = 1.65 and/0 = 6.0.
*It is sufficiently accurate to use the same coefficient of transmission for doors containing thin wood
panels as that of single panes of glass, namely, 1.13 Btu per hour per square foot per degree difference
between inside and outside air temperatures,
While most building materials have surfaces which show similar
characteristics as far as the transmission of heat is concerned, it is a well-
known fact that certain surfaces such as aluminum bronze, gold bronze,
aluminum foil, or in fact any metallic, highly polished surface presents a
greater resistance to heat transmission than the surface of the average
building material.
The greater heat resistance of such metallic surfaces is due primarily to
their higher reflectivity and consequent lower emissivity of radiant heat.
The use of multiple layers of metallic surfaces, combined with air spaces
of low resistance, provides a definite insulating effect. Factors2 for air
spaces bounded by aluminum foil are given in Table 2.
Coefficients of transmission of various types of wall, ceiling, floor and
roof construction with aluminum insulation can be readily calculated.
The present installation practice indicates that air spaces of J^ in. to
1J^ in. are preferred but manufacturers' recommendations should be
closely followed in the application of aluminum foil insulation.
The majority of the conductivities and conductances of the building
materials and insulations given in Table 2 were determined by the hot-
plate method of testing3. Attention is called to the fact that conductivi-
ties per inch of thickness of materials or insulations do not afford a true
basis for comparison, although they are frequently used for that purpose.
^Insulating Value of Bright Metallic Surfaces, by F. B. Rowley (A.S.H.V.E. Journal Section, Heating,
Piping and Air Conditioning, June, 1934, p. 263).
Standard Test Code for Heat Transmission through Walls (A.S.H.V.E. TRANSACTIONS, Vol. 34, 1928).
See also Chapter 40.
113
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Correct comparisons should take into consideration many different
factors, including conductivities or conductances, thicknesses installed
and manner of installation, while the selection of an insulation should also
give consideration to structural qualities, as well as to material and
application costs. Fire, vermin, and rot resistance are other important
factors to be considered when comparing materials. At present there is
no universally recognized method of rating insulations. Conductivities
and conductances of building materials and insulations are useful to the
heating engineer in determining over-all coefficients of heat transmission
of walls, floors, roofs and ceilings.
Computed Transmission Coefficients
Computed heat transmission coefficients of many common types of
building construction are given in Tables 3 to 13, inclusive, each con-
struction being identified by a serial number. For example, the coefficient
of transmission (U) of an 8-in. brick wall and }4 in. of plaster is 0.46, and
the number assigned to a wall of this construction is 1-B, Table 3.
Example 1. Calculate the coefficient of transmission (U) of an 8-in. brick wall with
14 in of piaster applied directly to the interior surface, based on an outside wind exposure
of 15 mph. It is assumed that the outside course is of face brick having a conductivity
of 9.20, and that the inside course is of common brick having a conductivity of 5.0, the
thicknesses each being 4 in. The conductivity of the plaster is assumed to be 3.3, and the
inside and outside surface coefficients are assumed to average 1.65 and 6.00, respectively,
for still air and a 15 mph wind velocity.
Solution, k (face brick) = 9.20; x = 4.0 in.; k (common brick) « 5.0; x « 4.0 in.;
k (plaster) - 3.3; x = H in.;/i = 1.65 ;/0 = 6.0. Therefore,
U
"6X) "*" 9.20 "*" 5.0 ""*" 3.3 T 1.65
1
" 0.167 + 0.435 4- 0.80 + 0.152 + 0.606
** 0.46 Btu per hour per square foot per degree Fahrenheit difference in tempera-
ture between the air on the two sides.
The coefficients in the tables were determined by calculations similar
to those shown in Example 1, using Fundamental Formulae 2, 3, 4 and 5
and the values of k (or Ca) , fi, fo and a indicated in Table 2 by asterisks.
In computing heat transmission coefficients of floors laid directly on the
ground (Table 10), only one surface coefficient (fi) is used. For example,
the value of U for a 1-in. yellow pine floor (actual thickness, 25/32 in.)
placed directly on 6-in. concrete on the ground, is determined as follows:
= 0.48 Btu per hour per square foot per degree difference
0.781 6.0
1.65 0.80 12.0
in temperature between the ground and the air immediately above the floor.
The thicknesses upon which the coefficients in Tables 3 to 13, inclusive,
are based are as follows :
Brick veneer ........................................................................................ 4 }n-
Plaster and metal lath ............. ', .......................................................... % m-
114
CHAPTER 5 — HEAT TRANSMISSION COEFFICIENTS AND TABLES
Plaster (on wood lath, plasterboard, rigid insulation, board
form, or corkboard) ................... . .................................................... 3^ in.
Slate (roofing) ............... „ ........ „ ........................................................... }/% in.
Stucco on wire mesh reinforcing ...................................................... 1 in.
Tar and gravel or slag-surfaced built-up roofing _______ ..................... % in.
1-in. lumber (S 2-S) ............................................................................ 2^2 ^
IJi-in. lumber (S-2-S) ............................................. Ijf6 in.
2-in lumber (S-2-S)... ..................................... . ................................... 1% in.
2H-in. lumber (S-2-S) ................................................................ 2j| in.
3-in. lumber (S-2-S) ............................................................................ 2% in.
4-in. lumber (S-2-S) ............................... . .......... . ....................... ... ..... .. 3 in.
Finish flooring (maple or oak) ........... .
Solid brick walls are based on 4-in. face brick and the remainder
common brick. Stucco is assumed to be 1-in. thick on masonry walls.
Where metal lath and plaster are specified, the metal lath is neglected.
Rigid insulation refers to the so-called board form which may be used
structurally, such as for sheathing. Flexible insulation refers to the
blankets, quilts or semi-rigid types of insulation.
Actual thicknesses of lumber are used in the computations rather than
nominal thicknesses. The computations for wood shingle roofs applied
over wood stripping are based on 1 by 4 in. wood strips, spaced 2 in. apart.
Since no reliable figures are available concerning the conductivity of
Spanish and French clay roofing tile, of which there are many varieties,
the figures for such types of roofs were taken the same as for slate roofs, as
it is probable that the values of U for these two types of roofs will
compare favorably.
The coefficients of transmission of the pitched roofs in Table 12 apply
where the roof is over a heated attic or top floor so the heat passes directly
ihrough the roof structure including whatever finish is applied to the
underside of the roof rafters.
Combined Coefficients of Transmission
If the attic is unheated, the roof structure and ceiling of the top floor
must both be taken into consideration, and the combined coefficient of
transmission determined. The formula for calculating the combined
coefficient of transmission of a top-floor ceiling, unheated attic space, and
pitched roof, per square foot of roof area, is as follows:
TJ Ur X Z7Ce (.
U = ttX£/r+Z7ce (6)
where
Z7r = coefficient of transmission of the roof.
Z7ce = coefficient of transmission of the ceiling.
n — the ratio of the area of the roof to the area of the ceiling.
In using this formula, a correction factor must be applied. As the
amount of heat transferred through an air space is proportional to the
difference of the fourth powers of the absolute temperatures of the surfaces
enclosing the air space, a greater amount of heat is absorbed or emitted
by radiation by the surfaces enclosing an unheated attic than by the
surfaces of a wall or ceiling in a room under still-air conditions, where the
surrounding objects are only slightly higher in temperature than the
interior surfaces of the walls and ceiling. For example, the average
115
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
coefficient of a surface in still air is 1.65 Btu per hour per square foot per
degree Fahrenheit, whereas the average coefficient of an air space in an
outside wall is about 1.10 Btu per hour per square foot per degree Fahren-
heit difference between the two surfaces, at a mean temperature of 40 F.
An air space coefficient of 1.10 is equivalent to a surface coefficient
of 2.20 for each of the two surfaces enclosing the air space, where the
over-all transmission is computed by using the coefficients of the two
surfaces enclosing the air space instead of the coefficient of the air space
itself. Hence, in determining the values of Ur and Z7Ce to be used in the
formula, the coefficients for the surfaces of the roof and ceiling enclosing
the attic should be increased to allow for the additional amount of heat
transferred by radiation, and a coefficient of 2.20 may be used with
sufficient accuracy for each of these surfaces, although in very precise
work a correction should be made to allow for the fact that the area of a
pitched roof over an unheated attic is greater than the area of the ceiling,
and hence, the amount of heat absorbed by radiation by each square foot
of roof surface is less than is given off by radiation by each square foot of
ceiling surface.
If the unheated attic space between the roof and ceiling has no dormers,
windows or vertical wall surfaces, the combined coefficients may be used
for determining the heat loss through the roof construction between the
attic and top-floor ceiling, but it should be noted that these coefficients
should be multiplied by the roof area and not by the ceiling area. If the
unheated attic contains windows, ventilators or vertical wall surfaces,
which would tend to reduce temperature in the attic to a temperature
approaching or equaling the outside temperature, the roof should be
neglected and only the top-floor ceiling construction and the correspond-
ing ceiling area taken into consideration, using the coefficients given in
Tables 8 or 9. Where there are no dormers, doors, or windows, and when
the transmission coefficients of the roof and the ceiling are approximately
the same, the value of the attic temperature may be taken as an average
between the inside and the outside temperature.
Basements and Unheated Rooms
The heat loss through floors into basements and into unheated rooms
kept closed may be computed by assuming a temperature for these rooms
of 32 F.
Additional information on the inside and outside temperatures to be
used in heat loss calculations is given in Chapter 7.
REFERENCES
A.S.H.V.E. research paper entitled Wind Velocity Gradients Near a Surface and Their Effect on Film
Conductance, by F. C. Houghten and Paul McDermott (A.S.H.V.E. TRANSACTIONS, Vol. 37, 1931).
A.S.H.V.E. research paper entitled Surface Conductances as Affected by Air Velocity, Temperature and
Character of Surface, by F. B. Rowley, A. B. Algren and J. L. Blackshaw (A.S.H.V.E. TRANSACTIONS,
Vol. 36, 1930).
A.S.H.V.E. research paper entitled Effects of Air Velocities on Surface Coefficients, by F. B. Rowley,
A. B. Algren and J. L. Blackshaw (A.S.H.V.E. TRANSACTIONS, Vol. 36, 1930).
A.S.H.V.E. research paper entitled Conductivity of Concrete, by F. C. Houghten and Carl Gutberlet
(A.S.H.V.E. TRANSACTIONS, Vol. 37, 1931).
A.S.H.V.E. research paper entitled Surface Coefficients as Affected by Direction of Wind, by F. B.
Rowley and W. A. Eckley (A.S.H.V.E. TRANSACTIONS, Vol. 37, 1931).
A.S.H.V.E. research paper entitled Thermal Resistance of Air Spaces, by F. B. Rowley and A. B. Algren
(A.S.H.V.E. TRANSACTIONS, Vol. 35, 1929).
116
CHAPTER 5 — HEAT TRANSMISSION COEFFICIENTS AND TABLES
A.S.H.V.E. research paper entitled The Heat Conductivity of Wood at Climatic Temperature Dif-
ferences, by F. B. Rowley (A.S.H.V.E. Journal Section, Heating, Piping and Air Conditioning, June, 1933).
A.S.H.V.E. research paper entitled Insulating Value of Bright Metallic Surfaces, by F. B. Rowley
(A.S.H.V.E. Journal Section, Heating, Piping and Air Conditioning, June, 1934).
Heat Transmission through Building Materials, by F. B. Rowley and A. B. Algren, University of Min-
nesota Engineering Experiment Station Bulletin No. 8.
Insulating Effect of Successive Air Spaces Bounded by Bright Metallic Surfaces, by L. W. Schad (A.S.H.-
V.E. TRANSACTIONS, Vol. 37, 1931).
Importance of Radiation in Heat Transfer through Air Spaces, by E. R. Queer (A.S.H.V.E. TRANS-
ACTIONS, Vol. 38, 1932).
Properties of Metal Foil as an Insulating Material, by J. L. Gregg (Refrigerating Engineering, May, 1932).
Thermal Insulation with Aluminum Foil, by R. B. Mason (Industrial and Engineering Chemistry,
March, 1933).
Heating, Ventilating and Air Conditioning, by Harding and Willard, Revised Edition, 1932.
Thermal Insulation of Buildings, Technical Paper No. 11 (American Architect, May, 1934).
House Insulation, Its Economies and Application, by Russell E. Backstrom (Report of the National
Committee on Wood Utilization, United States Government Printing Office, 1931).
Heat Insulation as Applied to Buildings and Structures, by E. A. Allcut, University of Toronto, 1934.
PROBLEMS IN PRACTICE
1 • What is the conductance of a 1-in. air space, faced with common building
materials, at a mean temperature of 50 F?
1.152 (Table 1).
2 • What is the conductivity of face brick?
9.20 (Table 2).
3 • What is the conductance of wood shingles?
1.28 (Table 2).
4 • What is the over-all coefficient of transmission U for a solid brick wall
12 -in. thick with plaster on wood lath, furred?
0.24 (Table 3, Wall 2C).
5 • Find the value of U for a 6-in. concrete wall with plaster on metal lath
attached to 2 -in. furring strips with flanged J-^-in. blanket insulation.
0.23 (Table 3, Wall 12L).
6 • Find the value of U for a wood siding wall with an interior finish of J£-in.
plaster on metal lath; sheathing thickness, 2%% in.
0.26 (Table 5, Wall 41B).
7 • What value of U should be used for a brick veneer wall with H-in. rigid
insulation sheathing finished on the interior with plaster on J^-in. rigid insu-
lation?
0.19 (Table 5, Wall 51D).
8 • What value of U should be used in computing the heat loss from an attic
through a floor of yellow pine on joists with a ceiling of metal lath and plaster?
0.30 (TableS, Floor 2B).
9 • What is the over-all heat transfer coefficient for a 6-in. concrete floor with
no insulation and with yellow pine flooring on sleepers resting on concrete?
0.33 (Table 10, Floor 2B).
10 • What is the coefficient U for a flat roof of 4-in. concrete with a metal lath
and plaster ceiling insulated with 1-in. cork board?
0.17 (Table 11, Roof 3N).
117
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
11 • A solid 12-in. common brick wall is finished on the inside with J^-in.
insulation plaster base, and J^-in. plaster; the plaster base is furred 1 in. from
the brick; k for insulating material = 0.34. Calculate the over-all coefficient
V.
fi = 1.65; /0 = 6.00; k for brick = 5.00; a for 1-in. air space = 1.1
Over-all heat resistance = R = -^ + ^ + rT + ~lf + 'ir== 5-703
l.OO O.O 1.1 O O
u = -4-
K
12 • A wall is built with two layers of >£-in. insulating material spaced 1 in.
apart; the air space is lined on one side with bright aluminum foil; mean
temperature is 40 F; still ah* on both sides of wall; k for insulating material
is 0.34. Calculate the value of U.
fi = 1.65; /0 = 1.65; a « 0.46
1 , 0.5 , 1 , 0.5 ,
- 6.327
~ 1.65 ^ 0.34 7 0.46 ^ 0.34 ' 1.65
U = 4- = °-158
JK.
13 • What is the inside surface temperature of a 6-in. solid concrete wall?
Inside air, 70 F; outside ah*, —20 F with 15 mph wind.
The temperature drop from point to point through a wall is directly proportional to the
heat resistance.
fi = 1.65; k for concrete = 12; /0 = 6.0
i ft i
Over-all resistance R = 1-5F + T7 + ^7i = L27
i.OO JLj£ O.U
Temperature drop, inside air to surface _ 1.65
Temperature drop, air to air 1.27
90
Temperature drop, inside air to surface = --.-^-rr ;, />r = 43 i
JL.Z/ ^\ I.uo
70 — 43 = 27 F, inside surface temperature of wall.
14 • How many inches of insulating material having a conductivity of 0.30
would be required, for the wall of Question 3, to raise the inside surface tem-
perature to 60 F?
Temperature drop, air to inside surface = 10 F; temperature drop, inside surface to out-
side air = 80 F. Therefore, the heat resistance from inside wall surface to outside air
must be eight times that from inside air to inside wall surface, or 8 X .. „* = 4.85. The
resistance for added material is, therefore,
- w + - 4'19
4.19 X 0.30 = 1.25 in. of insulation.
118
Chapter 6
AIR LEAKAGE
Nature of Air Infiltration, Air Leakage Through Walls, Window
Leakage, Wind Velocity to be Selected, Crack used for Computa-
tions, Multi-Story Buildings, Heat Equivalent of Air Entering
by Infiltration
AIR leakage losses are those resulting from the displacement of heated
air in a building by unheated outside air, the interchange taking
place through various apertures in the building, such as cracks around
doors and windows, fireplaces and chimneys. This leakage of air must be
considered in heating and cooling calculations. (See Chapters 7 and 8.)
THE NATURE OF AIR FILTRATION
The natural movement of air through building construction is due to
two causes. One is the pressure exerted by the wind; the other is the
difference in density of outside and inside air because of differences in
temperature.
The wind causes a pressure to be exerted on one or two sides of a
building. As a result, air comes into the building on the windward side
through cracks or porous construction, and a similar quantity of air
leaves on the leeward side through like openings. In general the resis-
tance to air movement is similar on the windward to that on the leeward
side. This causes a building up of pressure within the building and a
lesser air leakage than that experienced in single wall tests as determined
in the laboratory. It is assumed that actual building leakages owing to
this building up of pressure will be 80 per cent of laboratory test values.
While there are cases where this is not true, tests in actual buildings
substantiate the factor for the general case. Tests on mechanically
ventilated classrooms of average construction have shown that air
infiltration acts quite independently of the planned air supply. Accor-
dingly, the heating or cooling load owing to air infiltration from natural
causes should be considered in addition to the ventilating load.
The air exchange owing to temperature difference, inside to outside, is
not appreciable in low buildings. In tall, single story buildings with
openings near the ground level and near the ceiling, this loss must be
considered. Also in multi-storied buildings it. is a large item unless the
sealing between various floors and rooms is quite perfect. This tempera-
ture effect is a chimney action, causing air to enter through openings at
lower levels and to leave at higher levels.
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
A complete study of all of the factors involved in air movement through
building constructions would be very complex. Some of the complicating
factors are: the variations in wind velocity and direction; the exposure of
the building with respect to air leakage openings and with respect to
adjoining buildings; the variations in outside temperatures as influencing
the chimney effect; the relative area and resistance of openings on the
windward and leeward sides and on the lower floors and on the upper
floors; the influence of a planned air supply and the related outlet vents;
and the variation from the average of individual building units. A study
of infiltration points to the need for care in the obtaining of good building
construction, or unnecessarily large heat losses will result.
AIR LEAKAGE THROUGH WALLS
Table I1 gives data on infiltration through brick and frame walls. The
brick walls listed in this table are walls which show poor workmanship
and which are constructed of porous brick and lime mortar. For good
workmanship, the leakage through hard brick walls with cement-lime
mortar does not exceed one- third the values given. These tests indicate
that plastering reduces the leakage by about 96 per cent; a heavy coat of
cold water paint, 50 per cent; and 3 coats of oil paint carefully applied,
28 per cent. The infiltration through walls ranges from 6 to 25 per cent
of that through windows and doors in a 10-story office building, with
imperfect sealing of plaster at the baseboards of the rooms. With perfect
sealing the range is from 0.5 to 2.7 per cent or a practically negligible
quantity, which indicates the importance of good workmanship in proper
sealing at the baseboard. It will be noted from Table 1, that the in-
filtration through properly plastered walls can be neglected.
TABLE 1. INFILTRATION THROUGH WALLS
Expressed in cubic feet per square foot per hour*
WIND VBLOCTTT, MILES PER Hora
TYPE OP WALL
5
10
is
20
25
30
8« m. Brick WalL_{g£—L:
1.75
0.017
4.20
0.037
7.85
0.066
12.2
0.107
18.6
0.161
22.9
0.236
13 in. Brick Wall {$£^£1
1.44
0.005
3.92
0.013
7.48
0.025
11.6
0.043
16.3
0.067
21.2
0.097
Frame Wall, with lath and plasterb
0.03
0.07
0.13
0.18
0.23
0.26
aThe values in this table are 20 per cent less than test values to allow for building up of pressure in rooms
and are based on test data reported in A.S.H.V.E. research papers entitled Air Infiltration Through Various
Types of Brick Wall Construction, and Air Infiltration Through Various Types of Wood Frame Con-
struction. (See References on pages 128 and 129).
bWall construction: Bevel siding painted or cedar shingles, sheathing, building paper, wood lath and
3 coats gypsum plaster.
*Air Infiltration through Various Types of Brick Wall Construction, by Larson, Nelson and Braatz
A.S.H.V.E. TRANSACTIONS, Vol. 36r 1930).
120
CHAPTER 6 — AIR LEAKAGE
0 20 40 60 SO /OO /& i4O /6O /SO ZOO 22O 24O ^ffO 2BO 3OO
INFILTRATION w C FH. PER SQ. FT OF WALL
FIG. 1. INFILTRATION THROUGH VARIOUS TYPES OF SHINGLE CONSTRUCTION
The value of building paper when applied between sheathing and
shingles is indicated by Fig. 1, which represents the effect on outside
construction only, without lath and plaster. The effectiveness of plaster
properly applied is no justification for the use of low grade building paper
or of the poor construction of the wall containing it. Not only is it
difficult to secure and maintain the full effectiveness of the plaster but
also it is highly desirable to have two points of high resistance to air flow
with an air space between them.
^0.05
/OO /£0 MO S&> /8O
M9 C.f.M P£f9 5<>, FT. Of WALL
FIG. 2. INFILTRATION THROUGH SINGLE SURFACE WALLS USED IN FARM AND
OTHER SHELTER BUILDINGS
121
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
The amount of infiltration that may be expected through simple walls
used in farm and other shelter buildings, is shown in Fig. 2. The infil-
tration there indicated is that determined in the laboratory and should be
multiplied by the factor 0.80 to give proper working values.
WINDOW LEAKAGE
The amount of infiltration for various types of windows is given in
Table 2. The fit of double-hung wood windows is determined by crack
and clearance as illustrated in Fig. 3. The length of the perimeter opening
or crack for a double-hung window is equal to three times the width plus
two times the height, or in other words, it is the outer sash perimeter
length plus the meeting rail length. Values of leakage shown in Table 2
for the average double-hung wood window were determined by setting
the average measured crack and clearance found in a field survey of a
large number of windows on nine windows tested in the laboratory. In
addition, the table gives figures for a poorly fitted window. All of the
figures for double-hung wood windows are for the unlocked condition.
Just how a window is closed, or fits when it is closed, has considerable
influence on the leakage. The leakage will be high if the sash are short,
if the meeting rail members are warped, or if .the frame and sash are not
fitted squarely to each other. It is possible to have a window with
approximately the average crack and clearance that will have a leakage
at least double that of the figures shown. Values for the average double-
hung wood window in Table 2 are considered to be easily obtainable
figures provided the workmanship on the window is good. Should it be
known that the windows under consideration are poorly fitted, the larger
leakage values should be used. Locking a window generally decreases its
leakage, but in some cases may push the meeting rail members apart and
increase the leakage. On windows with large clearances, locking will
usually reduce the leakage.
Wood casement windows may be assumed to have the same unit
leakage as for the average double-hung wood window when properly
fitted. Locking, a normal operation in the closing of this type of window,
maintains the crack at a low value.
For metal pivoted sash, the length of crack is the total perimeter of the
movable or ventilating sections. Frame leakage on steel windows may be
neglected when they are properly grouted with cement mortar into brick
work or concrete. When they are not properly sealed, the linear feet of
sash section in contact with steel work at mullions should be figured at
25 per cent of the values for industrial pivoted windows as given in
Table 2.
Leakage values for storm sash are given in Figs. 4 and 5. When storm
sash are applied to well fitted windows, very little reduction in infiltration
is secured, but the application of the sash does give an air space which
reduces the heat transmission and helps prevent the frosting of the
windows. When storm sash are applied to poorly fitted windows, a
reduction in leakage of 50 per cent may be secured.
Doors vary greatly in fit because of their large size and tendency to
warp. For a well fitted door, the leakage values for a poorly fitted double-
hung wood window may be used. If poorly fitted, twice this figure should
122
CHAPTER 6 — AIR LEAKAGE
TABLE 2. INFILTRATION THROUGH WINDOWS
Expressed in Cubic Feet per Foot of Crack per Hour3-
TYPE OF WINDOW
REMARKS
WIND VELOCITY, MILES PER HOTTE
5
10
15
20
25
30
Double-Hung
Wood Sash
Windows
(Unlocked)
Around frame in masonry wall —
not calkedb
3.3
8.2
14.0
20.2
27.2
34.6
Around frame in masonry wall —
calkedb
0.5
1.5
2.6
3.8
4.8
5.8
Around frame in wood frame
construction D
2.2
6.2
10.8
16.6
23.0
30.3
Total for average window, non-
weatherstripped, Me-in. crack
and %4-in. clearance0. In-
cludes wood frame leakaged
6.6
21.4
39.3
59.3
80.0
103.7
Ditto, weatherstrippedd»
4.3
15.5
23.6
35.5
48.6
63.4
Total for poorly fitted window,
non-weatherstripped, % 2 -in .
crack and %2-in. clearance6.
Includes wood frame leakaged.
26.9
69.0
110.5
153.9
199.2
249.4
Ditto, weatherstrippedd
5.9
18.9
34.1
51.4
70.5
91.5
Double-Hung
Metal
WTindowsf
Non-weatherstripped, locked
Non-weatherstrippedr unlocked..
Weatherstripped, unlocked
20
20
6
45
47
19
70
74
32
96
104
46
125
137
60
154
170
76
Rolled
Section
Steel Sash
Windowsk
Industrial pi voted, s He-in. crack
Architectural projected,11 JNU-in.
crack.
52
20
14
8
108
52
32
24
176
88
52
38
244
116
76
54
304
152
100
72
372
208
128
96
Residential casement,1 J^2-in.
crack.
Heavy casement section, pro-
jected, J 3^2"in. crack.
Hollow Metal, vertically pivoted window*.
30
88
145
186
221
242
"The values given in this table are 20 per cent less than test values to allow for building up of pressure in
rooms, and are based on test data reported in the papers listed at the end of this chapter.
bThe values given for frame leakage are per foot of sash perimeter as determined for double-hung wood
windows. Some of the frame leakage in masonry walls originates in the brick wall itself and cannot be
prevented by calking. For the additional reason that calking is not done perfectly and deteriorates with
time, it is considered advisable to choose the masonry frame leakage values for calked frames as the average
determined by the calked and not-calked tests.
cThe fit of the average double-hung wood window was determined as }£-m. crack and %-in. clearance by
measurements on approximately 600 windows under heating season conditions.
dThe values given are the totals for the window opening per foot of sash perimeter and include frame
leakage and so-called elsewhere leakage. The frame leakage values included are for wood frame construction
but apply as well to masonry construction assuming a 60 per cent efficiency of frame calking.
*A J6-in. crack and clearance represents a poorly fitted window, much poorer than average.
^Windows tested in place in building.
^Industrial pivoted window generally used in industrial buildings. Ventilators horizontally pivoted
at center or slightly above, lower part swinging out.
^Architectural projected made of same sections as industrial pivoted except that outside framing member
is heavier, and refinements in weathering and hardware. Used in semi- monumental buildings such as schools.
Ventilators awing in or out and are balanced on side arms.
[Of same design and section shapes as sc-called heavy section casement but of lighter weight.
iMade of heavy sections. Ventilators swing in or out and stay set at any degree of opening.
kWith reasonable care in installation, leakage at contacts where windows are attached to steel frame-
work and at mulKons is negligible. With ?6-in. crack, representing poor installation, leakage at contact
with steel framework is about one-third, and at mullions about one-sixth of that given for industrial pivoted
windows in the table.
123
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
be used. If weathers tripped, the values may be reduced one-half. A
single door which is frequently opened, such as might be found in a store,
should have a value applied which is three times that for a well fitted
door. This extra allowance is for opening and closing losses and is kept
from being greater by the fact that doors are not used as much in the
coldest and windiest weather.
CHOOSING WIND VELOCITY
Although all authorities do not agree upon the value of the wind veloc-
ity that should be chosen for any given locality, it is common engineering
practice to use the average wind velocity during the three coldest months
of the year. Until this point is definitely established the practice of
using average values will be followed. Average wind velocities for the
months of December, January and February for various cities in the
United States and Canada are given in Table 2, Chapter 7.
FIG. 3. DIAGRAM ILLUSTRATING CRACK AND CLEARANCE
In considering both the transmission and infiltration losses, the more
exact procedure would be to select the outside temperature and the wind
velocity corresponding thereto, based on Weather Bureau records, which
would result in the maximum heat demand. Since the proportion of
transmission and infiltration losses varies with the construction and is
different for every building, the proper combination of temperature and
wind velocity to be selected would be different for every type of building,
even in the same locality. Furthermore, such a procedure would neces-
sitate a laborious cut-and-try process in every case in order to determine
the worst combination of conditions for the building under consideration.
It would also be necessary to consider heat lag due to heat capacity in the
case of heavy masonry walls, and other factors, to arrive at the most
accurate solution of the problem. Although heat capacity should be con-
sidered wherever possible, it is seldom possible to accurately determine the
worst combination of outside temperature and wind velocity for a given
building and locality. The usual procedure, as already explained, is to
select an outside temperature based on the lowest on record and the
average wind velocity during the months of December, January and
February.
The direction of prevailing winds may usually be included within an
angle of about 90 deg. The windows that are to be figured for prevailing
124
CHAPTER 6 — AIR LEAKAGE
12
a u
•? ad
1Q7
<u
§02
<
50.03
45.63
40.83
35.4Q
ZdSO
,
J
C
f
d
JA
1
d
j
\
1
I
/
1
1
/
I
1
1
f
i
1
1
1
1
/
1
J
1
1
j
1
/
j
I
It
A -WITHOUT STORM SASH
8* STORM SASH- SUSPENDED
C- STORM SASH-fASTEMEQ
WITH FOUR TURN BUTTONS
D- SAME As C WITH WOOL
WEATHEZ-STR/P APPLIED
To STORM SASH
y
I
/
I
1
f
/
I
II
-
1 >
/
1
—
j
I
/
//
/
ty
0
1
$
1
jp
-> 50 KX> ISO 200 Z5Q 300
INFILTRATION CJ:H.Pex roar GrOwcx
FIG. 4.
INFILTRATION THROUGH SASH PERIMETER OF WINDOW WITH AND WITHOUT
STORM SASH — J^4-iN. CRACK AND jH?2-iN. CLEARANCE
and non-prevailing winds will ordinarily each occupy about one-half the
perimeter of the structure, the proportion varying to a considerable extent
with the plan of the structure. (See discussion of wind movement in
Chapter 4.)
LZ
07
(26
*Q4
50
A*W/THOUT STORM SASH
5- STORM SASH • SUSPENDED
C * 'STORM SASH • FASTENED
Wrrn Foue TURN BUTTONS
JOO 150 200 Z50 500 350
INFIUTZATION Cf.H. PER FOOT OF CRACK
400
50.03
45.65
2430
i
FIG. 5. INFILTRATION THROUGH SASH PERIMETER OF WINDOW WITH AND WITHOUT
STORM SASH— K-*N< CRACK AND J^-IN. CLEARANCE
125
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
CRACK USED FOR COMPUTATIONS
In no case should the amount of crack used for computation be less
than half of the total crack in the outside walls of the room. Thus, in a
room with one exposed wall, take all the crack; with two exposed walls,
take the wall having the most crack ; and with three or four exposed walls,
take the wall having the most crack ; but in no case take less than half the
total crack. For a building having no partitions, whatever wind enters
through the cracks on the windward side must leave through the cracks
on the leeward side. Therefore, take one-half the total crack for com-
puting each side and end of the building.
The amount of air leakage is sometimes roughly estimated by assuming
a certain number of air changes per hour for each room, the number of
changes assumed being dependent upon the type, use and location of the
room, as indicated in Table 3. This method may be used to advantage as
a check on the calculations made in the more exact manner.
TABLE 3. AIR CHANGES TAKING PLACE UNDER AVERAGE CONDITIONS EXCLUSIVE
OF AIR PROVIDED FOR VENTILATION
KIND OF BOOM OB BUILDING
NUMBER OP Am CHANGES
TAKING PLACE
PER HOUR
Rooms, 1 side exposed
1
Rooms, 2 sides exposed
\y>
Rooms, 3 sides exposed
2
Rooms 4 sides exposed
2
Rooms with no windows or outside doors
lAto %
Entrance Halls
2 to 3
Reception Halls
2
Living Rooms
1 to 2
Dining Rooms .
1 to 2
Bath Rooms
2
Drug Stores
2 to 3
Clothing Stores
1
Churches, Factories, Lofts, etc.
% to 3
MULTI-STORY BUILDINGS
In tall buildings, infiltration may be considerably influenced by tem-
perature difference or chimney effect which will operate to produce a
head that will add to the effect of the wind at lower levels and subtract
from it at higher levels.2 On the other hand, the wind velocity at lower
levels may be somewhat abated by surrounding obstructions. Further-
more, the chimney effect is reduced in multi-story buildings by the partial
isolation of floors preventing free upward movement, so that wind and
temperature difference may seldom cooperate to the fullest extent.
Making the rough assumption that the neutral zone is located at mid-
*Influence of Stack Effect on the Heat Loss in Tall Buildings, by Axel Marin (A.S.H.V.E. Journal
Section, Heating, Piping and Air Conditioning* August, 1934, p. 349).
126
CHAPTER 6 — AIR LEAKAGE
height of a building, and that the temperature difference is 70 F, the
following formulae may be used to determine an equivalent wind velocity
to be used in connection with Tables 1 and 2 that will allow for both wind
velocity and temperature difference:
- 1.75 a (1)
-f- 1.75 b (2)
where
Me = equivalent wind velocity to be used in conjunction with Tables 1 and 2.
M = wind velocity upon which infiltration would be determined if tem-
perature difference were disregarded.
a = distance of windows under consideration from mid-height of building
if above mid-height.
b = distance if below mid-height.
The coefficient 1.75 allows for about one-half the temperature difference head.
For buildings of unusual height, Equation 1 would indicate negative
infiltration at the highest stories, which condition may, at times, actually
exist, although probably no greater wind velocities should be figured at
such extremely high levels3.
Sealing of Vertical Openings4
In tall, multi-story buildings, every effort should be made to seal off
vertical openings such as stair-wells and elevator shafts from the re-
mainder of the building. Stair-wells should be equipped with self-closing
doors, and in exceptionally high buildings, should be closed off into
sections of not over 10 floors each. Plaster cracks should be filled.
Elevator enclosures should be tight and solid doors should be used.
If 'the sealing of the vertical openings is made effective, no allowance
need be made for the chimney effect. Instead, the greater wind move-
ment at the high altitudes makes it advisable to install additional heating
surface on the upper floors above the level of neighboring buildings, this
additional surface being increased as the height is increased. One
arbitrary rule is to increase the heating surface on floors above neighboring
buildings by an amount ranging from 5 per cent to 20 per cent. This extra
heating surface is required only on the windward side and on windy days,
and hence automatic temperature control is especially desirable with such
installations.
Heating Surface for Stair- Wells4
In stair-wells that are open through many floor levels although closed
off from the remainder of each floor by doors and partitions, the strati-
fication of air makes it advisable to increase the amount of heating surface
at the lower levels and to decrease the amount at higher levels even to the
point of omitting all heating surface on the top several floor levels. One
rule is to calculate the heating surface of the entire stair- well in the usual
3Wind Velocities Near a Building and Their Effect on Heat Loss, by F. C. Houghten, J. L. Blackshaw,
and Carl Gutberlet (A.S.H,V.E. Journal Section, Healing, Piping and Air Conditioning, September, 1934).
*See Flue Action in Tall Buildings, by H. L. Alt (Heating, Piping and Air Conditioning, May, 1932).
127
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
way and to place 50 per cent of this in the bottom third, the normal
amount in the middle third and the balance in the top third.
HEAT EQUIVALENT OF AIR ENTERING BY INFILTRATION
The heat required to warm cold, outside air, which enters a room by
infiltration, to the temperature of the room is given by the following
equation :
Hi « 0.24 Q d (t - t0) (3)
where
Hi = Btu per hour required for heating air leaking Into building from
outside temperature t0 to inside temperature /.
Q — cubic feet of air entering per hour at inside temperature /.
d = density (pounds per cubic foot) of air at inside temperature t.
t = inside temperature at the proper level.
t0 — outside air temperature for which heating system is designed.
0.24 = specific heat of air.
It is sufficiently accurate to take d — 0.075 Ib, in which case the equa-
tion reduces to
Hi = 0.018 Q(t- t0) (4)
While a heating reserve must be provided to warm inleaking air on
the windward side of a building, this does not necessarily mean that the
heating plant must be provided with a reserve capacity, since the inleaking
air, warmed at once by adequate heating surface in exposed rooms, will
move transversely and upwardly through the building, thus relieving
other radiators of a part of their load. The actual loss of heat of a building
caused by infiltration is not to be confused with the necessity for pro-
viding additional heating capacity for a given space. Infiltration is a
disturbing factor in the heating of a building, and its maximum effect
(maximum in the sense of an average of wind velocity peaks during the
heating season above some reasonably chosen minimum) must be met
by a properly distributed reserve of heating capacity, which reserve, how-
ever, is not in use at all places at the same time, nor in any one place at
all times.
REFERENCES
Air Leakage, by Houghten and Schrader (A.S.H.V.E. TRANSACTIONS, Vol. 30, 1924).
Air Infiltration through Various Types of Brick Wall Construction, by Larson, Nelson and Braatz
(A.S.H.V.E. TRANSACTIONS, Vol. -85, 1929).
Infiltration through Plastered and Unplastered Brick Walls, by F. C. Houghten and Margaret Ingels
(A.S.H.V.E. TRANSACTIONS, Vol. 33, 1927).
Air Leakage around Window Openings, by C. C- Schrader (A.S.H.V.E. TRANSACTIONS, Vol. 30, 1924).
Effect of Frame Calking and Storm Sash on Infiltration around and through Windows, by Richtrnann
and Braatz (A.S.H.V.E. TRANSACTIONS, Vol. 34, 1928).
Air Leakage on Metal Windows in a Modern Office Building, by Houghten and O'Connell (A.S.H.V.E,
TRANSACTIONS, Vol. 34, 1928).
' The Weathertightness of Rolled Section Steel Windows, by Emswiler and Randall (A.S.H.V.E. TRANS-
ACTIONS, Vol. 34, 1928).
Air Leakage through a Pivoted Metal Window, by Houghten and O'Connell (A.S.H.V.E. TRANSACTIONS,
Vol. 34, 1928).
Pressure Difference across Windows in Relation to Wind Velocity, by Emswiler and Randall (A.S.H.V.E.
TRANSACTIONS, Vol. 35, 1929).
128
CHAPTER 6 — AIR LEAKAGE
Air Infiltration Through Various Types of Wood Frame Construction, by Larson, Xelson and Braatz
(A.S.H.V.E. TRANSACTIONS, Vol. 36, 1930).
Neutral Zone in Ventilating, by J. E. Emswiler (A.S.H.V.E. TRANSACTIONS, Vol. 32, 1920).
Air Infiltration Through Double-Hung Wood Windows, by Larson, Nelson and Kubasta (A.S.H.V.E.
TRANSACTIONS, Vol. 37, 1931).
Flue Action in Tall Buildings, by H. L. Alt (Heating, Piping and Air Conditioning, May, 1932;.
Air Infiltration Through Steel Framed Windows, by D. O. Rusk, V. H. Cherry and L. Boelter (Heating,
Piping and Air Conditioning, October, 1932).
Investigation of Air Outlets in Class Room Ventilation, by Larson, Nelson, and Kubasta (A.S.H.V.E.
TRANSACTIONS, Vol. 38, 1932).
PROBLEMS IN PRACTICE
1 • What are the causes of infiltration (or exfiltration) and how do they act
on a building?
The wind and temperature differences create differences between internal and external
pressures which cause air to flow through any openings in the walls.
2 • Why is it essential to consider this in heating calculations?
The inflowing air displaces inside heated air and must be heated up to the internal
temperature.
3 • Where is it necessary to consider infiltration created by temperature
difference?
In tall, single-story buildings and in multi-story buildings where the floors are not
adequately isolated.
4 • Why is the infiltration in a building less than that determined in laboratory
tests?
In laboratory tests, the indicated wind velocity is measured by the difference in pressure
on the two sides of a single wall, window, or object tested. In a building, an internal
back pressure is built up between its walls to a point where outflow on the lee side is equal
to inflow on the windward side and this back pressure reduces the actual inflow below
that determined in the laboratory for a comparable wind.
5 • Is heat loss by infiltration through walls of importance?
Only in the case of simple walls or poorly constructed compound walls.
6 • What measurements are required to calculate the heat loss through double-
hung wood windows?
Sash crack (equal to the sash perimeter plus the meeting rail) and frame crack (equal
to the frame perimeter).
7 • What is the basis for selecting the wind velocity and outside temperature
to be used in making infiltration calculations?
Weather Bureau records. The wind velocity taken is the average during the three
coldest months and the temperature used is the lowest on record for the given locality.
8 • How does the temperature difference influence the heat loss in a tali
building?
The chimney effect caused by the temperature difference operates to produce a head that
will add to the effect of the wind at lower levels and subtract from it at higher levels.
9 • For a wind velocity of 15 mph and a building 180 ft high, calculate the
effective wind velocity at the ground floor and at a height of 150 ft.
a. At the ground floor the effective wind velocity would be
Me = Vl52 + 1.75 X 90 = 19.6 mph
129
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
b. At a floor 150 ft above the ground
Me = Vl52 - 175 X 60 = 11.0 mph
10 • A room contains three 2 ft -8 in. by 5 ft-6 in. plain double-hung wood win-
dows with Jle-hi. crack and %4-in. clearance. Assume a wind velocity of
20 mph and a temperature difference of 75 F. Neglecting chimney effect, what
is the maximum heat loss due to infiltration?
From Table 2, heat loss per foot of crack per degree temperature difference is 1.067 Btu
per hour. Length of crack for the three windows is 57 ft. The maximum heat loss, due
to infiltration, is equal to 1.067 X 57 X 75 or 4561 Btu per hour.
11 • Find the infiltration through a wall with 16-in. shingles on 1 in. by 4 in.
hoards w^th 20 mph wind velocity. Give the pressure drop through the wall.
Referring to Curve 3C, Fig. 1, the value on the horizontal scale corresponding to 20 mph
is approximately 102 cfh per square foot of wall.
The pressure drop through the wall is 0.193 in. of water (see left hand vertical scale).
12 • What will be the infiltration through air-dried end and side-matched
sheathing for 15 mph wind velocity?
Referring to Curve IOC, Fig. 2, the value on the horizontal scale corresponding to
15 mph is 50 cfh per square foot of wall.
13 • From Table 2, find the infiltration (cubic feet per hour per foot of crack)
for an average double-hung window, not weather stripped, with a 20 mph
wind velocity.
59.3 cu ft per foot of crack per hour.
14 • Using the value found in Question 11, what will be the heat requirement
in a building with a total crack (all windows and doors) of 180 ft if the wind
velocity is 15 mph, the outside temperature is 0 F, and the inside temperature
is 70 F?
Using one half of the total crack, the volume of air is:
90 X 59.3 = 5337 cu ft
H - 0.018 X 5337 X (70 - 0) = 6724.6 Btu. (See Equation 4.)
130
Chapter 7
HEATING LOAD
Factors Governing Heat Demand, Procedure, Temperatures,
Wind Movement, Heat Sources Other Than Heating Plant,
Example, Condensation
design any system of heating, the maximum probable heat demand
JL must be accurately estimated in order that the apparatus installed
shall be capable of maintaining the desired temperature at all times. The
factors which govern this maximum heat demand — most of which are
seldom, if ever, in equilibrium — include the following:
1. Outside temperature.
2. Rain or snow.
3. Sunshine or cloudiness.
4. Wind velocity.
5. Heat transmission of exposed parts of building.
6. Infiltration of air through cracks, crevices and
open doors and windows.
7. Heat capacity of materials.
8. Rate of absorption of solar radiation by exposed
materials.
9. Inside temperatures.
10. Stratification of air.
11. Type of heating system.
12. Ventilation requirements.
13. Period and nature of occupancy.
14. Temperature regulation.
Outside Conditions
(The Weather}
Building
Construction
Inside
Conditions
The inside conditions vary from time to time, the physical properties of
the building construction may change with age, and the outside conditions
are changing constantly. Just what the worst combination of all of these
variable factors is likely to be in any particular case is therefore con-
jectural. Because of the nature of the problem, extreme precision in
estimating heat losses at any time, while desirable, is hard of attainment.
The procedure to be followed in determining the heat loss from any
building can be divided into seven consecutive steps, as follows:
1. Determine on the inside air temperature, at the breathing line or the 30-in. line,
which is to be maintained in the building during the coldest weather. (See Table 1.)
2. Determine on an outside air temperature for design purposes, based on the minimum
temperatures recorded in the locality in question, which will provide for all but the
most severe weather conditions. Such conditions as may exist for only a few consecu-
tive hours are readily taken care of by the heat capacity of the buHtKng Itself.
(See Table 2.)
131
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
3 Select or compute the heat transmission coefficients for outside walls and glass;
also for inside walls, floors, or top-floor ceilings, if these are next to unheated space;
include roof if next to heated space. (See Chapter 5.)
4 Measure up net outside wall, glass and roof next to heated spaces, as well as any
cold walls, floors or ceilings next to unheated space. Such measurements are made from
building plans, or from the actual building.
5. Compute the heat transmission losses for each kind of wall, glass, floor, ceiling
and roof in the building by multiplying the heat transmission coefficient in each case
by the area of the surface in square feet and the temperature difference between the
inside and outside air. (See Items 1 and 2.)
6. Select unit values and compute the heat equivalent of the infiltration of cold air
taking place around outside doors and windows. These unit values depend on the kind or
width of crack and wind velocity, and when multiplied by the length of crack and the
temperature difference between the inside and outside air, the result expresses the heat
required to warm up the cold air leaking into the building per hour, (bee Chapter b.)
7. The sum of the heat losses by transmission (Item 5) through the outside wall and
glass as well as through any cold floors, ceilings or roof, plus the heat equivalent (Item 6)
of the cold air entering by infiltration represents the total heat loss equivalent for any
building.
Item 7 represents the heat losses after the building is heated and under
stable operating conditions in coldest weather. Additional heat is
required for raising the temperature of the air, the building materials and
the material contents of the building to the specified standard inside
temperature.
The rate at which this additional heat is required depends upon the
heat capacity of the structure and its material contents and upon the
time in which these are to be heated.
This additional heat may be figured and allowed for as conditions re-
TABLE 1. WINTER INSIDE DRY-BULB TEMPERATURES USUALLY SPECiFiEDa
TYPE OP BUILDING
DEO FAER
TYPE OP BUILDING
DBG F^
SCHOOLS
Class rooms
Assembly rooms
Gymnasiums
Toilets and baths
Wardrobe and locker rooms „
Kitchens
Dining and lunch rooms
Playrooms
Natatoriums™
HOSPITALS —
Private rooms
Private rooms (surgical)
Operating rooms
Wards -
Kitchens and laundries
Toilets
Bathrooms
70-72
68-72
55-65
70
65-68
66
65-70
60-65
75
70-72
70-80
70-95
68
66
68
70-80
THEATERS —
Seating space..
Lounge rooms..
Toilets
HOTELS —
Bedrooms and baths
Dining rooms
Kitchens and laundries....
Ballrooms
Toilets and service rooms..
HOMES -
STORES
PUBLIC BUILDINGS-
WARM AIR BATHS
STEAM BATHS
FACTORIES AND MACHINE SHOPS
FOUNDRIES AND BOILER SHOPS
PAINT SHOPS
68-72
68-72
68
70
70
66
65-68
70-72
65-68
68-72
120
110
60-65
50-60
80
aThe most comfortable dry-bulb temperature to be maintained depends on the relative humidity and
air motion. These three factors considered together constitute what ts termed the effective temperature.
See Chapter 2.
132
CHAPTER 7 — HEATING LOAD
quire, but inasmuch as the heating system proportioned for taking care
of the heat losses will usually have a capacity about 100 per cent greater
than that required for average winter weather, and inasmuch as most
buildings may either be continuously heated or have more time allowed
for heating-up during the few minimum temperature days, no allowance
is made except in the size of boilers or furnaces.
INSIDE TEMPERATURES
The inside air temperature which must be maintained within a building
and which should always be stated in the heating specifications is under-
stood to be the dry-bulb temperature at the breathing line, 5 ft above the
floor, or the 30-in. line, and not less than 3 ft from the outside walls.
Inside air temperatures, usually specified, vary in accordance with the use
to which the building is to be put and Table 1 presents values which con-
form with good practice.
The proper dry-bulb temperature to be maintained depends upon the
relative humidity and air motion, as explained in Chapter 2. In other
words, a person may feel warm or cool at the same dry-bulb temperature,
depending on the relative humidity and air motion. The optimum winter
effective temperature for sedentary persons, as determined at the A.S.H.
V.E. Research Laboratory, is 66 deg.1
According ^ to Fig. 2, Chapter 2, for so-called still air conditions, a
relative humidity of approximately 50 per cent is required to produce an
effective temperature of 66 deg when the dry-bulb temperature is 70 F.
However, even where provision is made for artificial humidification, the
relative humidity is seldom maintained higher than 40 per cent during the
extremely cold weather, and where no provision is made for humidifica-
tion, the relative humidity may be 20 per cent or less. Consequently, in
using the figures given in Table 1, consideration should be given to
whether provision is to be made for humidification, and if so, the actual
relative humidity to be maintained.
Temperature at Proper Level: In making the actual heat-loss compu-
tations, however, for the various rooms in a building it is often necessary
to modify the temperatures given in Table 1 so that the air temperature
at the proper level will be used. By air temperature at the proper level is
meant, in the case of walls, the air temperature at the mean height be-
tween floor and ceiling; in the case of glass, the air temperature at the
mean height of the glass; in the case of roof or ceiling, the air temperature
at the mean height of the roof or ceiling above the floor of the heated
room; and in the case of floors, the air temperature at the floor level. In
the case of heated spaces adjacent to unheated spaces, it will usually be
sufficient to assume the temperature in such spaces as the mean between
the temperature of the inside heated spaces and the outside air tempera-
ture, excepting where the combined heat transmission coefficient of the
roof and ceiling can be used, in which case the usual inside and outside
temperatures should be applied. (See discussion regarding the use of
combined coefficients of pitched roofs, unheated attics and top-floor
ceilings Chapter 5.)
*See Chapter 2, p. 43.
133
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
High Ceilings: Research data concerning stratification of air in build-
ings are lacking, but in general it may be said that where the increase in
temperature is due to the natural tendency of the warmer or less dense
air to rise, as where a direct radiation system is installed, the temperature
of the air at the ceiling increases with the ceiling height. The relation,
however, is not a straight-line function, as the amount of increase per foot
of height apparently decreases as the height of the ceiling increases, ac-
cording to present available information.
Where ceiling heights are under 20 ft, it is common engineering practice
to consider that the Fahrenheit temperature increases 2 per cent for each
foot of height above the breathing line. This rule, sufficiently accurate
for most cases, will give the probable air temperature at any given level
for a room heated by direct radiation. Thus, the probable temperature
in a room at a point three feet above the breathing line, if the breathing
line temperature is 70 F, will be
(1.00 + 3 X .02) 70 = 74.2 F.
With certain types of heating and ventilating systems, which tend to
oppose the natural tendency of warm air to rise, the temperature differ-
ential between floor and ceiling can be greatly reduced. These include
unit heaters, fan-furnace heaters, and the various types of mechanical
ventilating systems. The amount of reduction is problematical in certain
instances, as it depends upon many factors such as location of heaters,
air temperature, and direction and velocity of air discharge. In some
cases it has been possible to reduce the temperature between the floor
and ceiling by a few degrees, whereas, in other cases, the temperature at
the ceiling has actually been increased because of improper design, instal-
lation or operation of equipment. So much depends upon the factors
enumerated that it is not advisable to allow less than 1 per cent per foot
(and usually more) above the breathing line in arriving at the air tem-
perature at any given level for any of these types of heating and ventilating
systems, unless the manufacturers are willing to guarantee that the par-
ticular type of equipment under consideration will maintain a smaller
temperature differential for the specific conditions involved.
Temperature at Floor Level: In determining mean air temperatures
just above floors which are next to ground or unheated spaces, a tempera-
ture 5 deg lower than the breathing-line temperature may be used, pro-
vided the breathing-line temperature is not less than 55 F.
OUTSIDE TEMPERATURES
The outside temperature used in computing the heat loss from a build-
ing is seldom taken as the lowest temperature ever recorded in a given
locality. Such temperatures are usually of short duration and are rarely
repeated in successive years. It is therefore evident that a temperature
somewhat higher than the lowest on record may be properly assumed in
making the heat-loss computations.
The outside temperature to be assumed in the design of any heating
system is ordinarily not more than 15 deg above .the lowest recorded tem-
perature as reported by the Weather Bureau during the preceding 10
years for the locality in which the heating system is to be installed. In
134
CHAPTER 7 — HEATING LOAD
the case of massive and well insulated buildings in localities where the
minimum does not prevail for more than a few hours, or where the lowest
recorded temperature is extremely unusual, more than 15 deg above the
minimum may be allowed, due primarily to the fly -wheel effect of the heat
capacity of the structure. The outside temperature assumed and used in
the design should always be stated in the heating specifications. Table 2
lists the coldest dry-bulb temperatures ever recorded by the Weather
Bureau at the places listed.
If Weather Bureau reports are not available for the locality in question,
then the reports for the station nearest to this locality are to be used,
unless some other temperature is specifically stated in the specifications.
In computing the average heat transmission losses for the heating season
in the United States the average outside temperature from October 1
to May 1 should be used.
WIND MOVEMENT
Trie effect of wind on the heating requirements of any building should
be given consideration under two heads:
1. Wind movement increases the heat transmission of walls, glass, and roof, affecting
poor walls to a much greater extent than good walls.
2. Wind movement materially increases the infiltration (inleakage) of cold air through
the cracks around doors and windows, and even through the building materials them-
selves, if such materials are at all porous.
Theoretically as a basis for design, the most unfavorable combination
of temperature and wind velocity should be chosen. It is entirely possible
that a building might require more heat on a windy day with a moderately
low outside temperature than on a quiet day with a much lower outside
temperature. However, the combination of wind and temperature which
is the worst would differ with different buildings, because wind velocity
has a greater effect on buildings which have relatively high infiltration
losses. It would be possible to work out the heating load for a building
for several different combinations of temperature and wind velocity which
records show to have occurred and to select the worst combination ; but
designers generally do not feel that such a degree of refinement is justified.
Therefore, pending further studies of actual buildings, it is recommended
that the average wind movement in any locality during December,
January and February be provided for in computing (1) the heat trans-
mission of a building, and (2) the heat required to take care of the infiltra-
tion of outside air.
The first condition is readily taken care of, as explained in Chapter 5,
by using a surface coefficient /0 for the outside wall surface which is based
on the proper wind velocity. In case specific data are lacking for any
given locality, it is sufficiently accurate to use an average wind velocity of
approximately 15 mph which is the velocity upon which the heat trans-
mission coefficient tables in Chapter 5 are based.
In a similar manner, the heat allowance for infiltration through cracks
and walls (Tables 1 and 2, Chapter 6) must be based on the proper wind
velocity for a given locality. In the case of tall buildings special attention
must be given to infiltration factors. (See Chapter 6).
In the past many designers have used empirical exposure factors which
135
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 2. CLIMATIC CONDITIONS COMPILED FROM WEATHER BUREAU RECORDS
COL. A
COL. B
COL. C
COL. D
COL. E
COL. F
State
City
Average
Temp.,
Oct. 1st-
May 1st
Lowest
Tempera-
ture
Ever
Reported
Average
Wind Vel-
ocity Dec.,
Jan., Feb..
Miles per
Hour
Direction
of Prevail-
ing Wind,
Dec.. Jan.,
Feb.
Ala
Mobile
57.7
^
8.3
N
Birmingham
53.9
-10
8.6
N
Ariz
Phoenix.
59.5
12
3.9
E
Flagstaff
34.9
—25
6.7
SW
Ark
Fort Smith
49.5
—15
8.0
E
Calif
Little Rock.
San Francisco
51.6
54.3
-12
27
9.9
7.5
NW
N
Los Ansreles .
58.6
28
6.1
NE
Colo
" o**"** .— ... ...... ... .
Denver
39.3
—29
7.4
s
Conn
Grand Junction
New Haven
39.2
38.0
-21
-15
5.6
9.3
SE
N
D. C.
Washington ... . _
43.2
-15
7.3
NW
Fla
Jacksonville
61.9
10
8.2
NE
Ga
Atlanta ......
51.4
—8
11.8
NW
Idaho ..
Savannah
Lewiston „
58.4
42.5
8
-23
8.3
4.7
NW
E
Pocatello
36.4
—22
9.3
SE
Ill
Chicago
Springfield
36.4
39.9
-23
-24
17.0
10.2
SW
NW
Ind
Indianapolis
Evansville
40.2
44.1
-25
— 16
11.8
8.4
S
s
Iowa
Kans.
Dubuque
Sioux City
Concordia
33.9
32.1
38.9
-32
-35
-25
6.1
12.2
7.3
NW
NW
N
Dodge Citv
40.2
—26
10.4
NW
Ky. ~ .
La.
^ v .»^ .„ y —
Louisville
New Orleans
45.2
61.5
-20
7
9.3
9.6
SW
N
Me
Md.
Shreveport
Eastport .
Portland
Baltimore
56.2
31.1
33.6
43.6
-5
-23
-21
7
7.7
13.8
10.1
7.2
SE
W
NW
NW
Mass.
Mich.
Boston .
Alpena. .
37.6
29.1
-18
-28
11.7
11.3
W
W
Detroit-
Marquette
35.4
27.6
-24
—27
13.1
11.4
SW
NW
Minn.
Duluth
Minneapolis
25.1
29.6
-41
—33
11.1
11.5
SW
NW
Miss
Mo.
Vicksburg
St. Joseph
56.0
40.3
-1
—24
7.6
9.1
SE
NW
St. Louis
43.3
—22 '
11.8
NW
Springfield
43.0
—29
11.3
SE
Mont
Billings
34.7
-49
W
Havre
27.7
—57
8.7
SW
Nebr
Lincoln
37.0
-29
10.9
N
North Platte
34.6
-35
9.0
W
Nev
Tonopah
39 6
— 10
9 9
SE
Winnemucca
37.9
-28
9.5
NE
N. H.._
Concord _
33.4
-35
6.0
NW
N. J.
Atlantic City
41.6
—9
10.6
NW
N.Y..Z1L..
Albany
Buffalo
35.1
34.7
-24
-20
7.9
17.7
S
W
N. M
New York.
Santa Fe _
40.7
38.0
-14
-13
17.1
7.3
NW
NE
136
CHAPTER 7 — HEATING LOAD
TABLE 2. CLIMATIC CONDITIONS COMPILED FROM WEATHER BUREAU RECORDS —
(Continued)
COL. A
COL. B
COL. C
COL. D
COL. E
COL. F
State
or
Province
City
Average
Temp.,
Oct. 1st-
May 1st
Lowest
Tempera-
ture
Ever
Reported
Average
Wind Vel-
ocity Dec.,
Jan., Feb.,
Miles per
Hour
Direction
of Prevail-,
ing Wind,
Dec., Jan.,
Feb.
N C
Raleigh
49.7
53.1
24.5
18.9
36.9
39.9
48.0
34.1
45.9
41.9
40.8
37.6
56.9
53.7
28.1
32.3
47.0
50.9
53.0
54.7
60.7
38.1
40.0
29.3
49.1
45.2
47.4
45.3
37.5
38.8
41.9
28.6
31.2
33.0
31.0
28.9
23.3
43.8
41.7
17.2
27.1
35.5
32.5
26.9
21.6
32.0
30.1
27.4
24.4
14.7
1.6
-2
5
-45
-44
-17
-20
-17
-24
-2
-6
' -20
-17
7
-2
-43
-34
-16
-9
-2
-8
4
-24
-20
-28
2
-7
-3
3
-30
-28
-27
-36
-43
-25
-45
-40
-57
-2
2
-46
35
7.3
8.9
liTi
14.5
9.3
12.0
6.0
6.5
11.0
13.7
14.6
11.0
8.0
11.5
7.5
6.5
9.6
10.5
11.0
8.2
8.9
4.9
12.9
9.0
5.2
7.4
9.1
5.2
4.8
6.6
12.8
5.6
11.7
5.3
3.0
4.5
8.9
4.2
12.4
8.7
13.0
SW
SW
NW
W
sw
sw
N
SE
S
NW
NW
NW
N
NE
NW
W
SW
NW
NW
NW
N
W
SE
S
N
NW
S
SE
SW
W
S
SW
NW
W
NW
NE
W
N
E
SW
NW
NW
W
SW
NW
SW
sw
sw
N. Dak.,..
Ohio
Okla
Wilmington
Bismarck.-
Devils Lake
Cleveland ~
Columbus
Oklahoma City
Oree
Baker
Pa
Portland.
Philadelphia
R. I
Pittsburgh
Providence
S C.
Charleston
S. Dak
Te/m
Texas
Columbia
Huron
Rapid City
Knoxville
Memphis -
El Paso
Utah
Fort Worth. _
San Antonio
Modena
Vt
Salt Lake City
Burlington
Va
Norfolk
Wash
Lynchburg
Richmond
Seattle.-
W. Va
Spokane
Elkins.
Wis
Parkersburg
Green Bay
Wyo
La Crosse
Milwaukee
Sheridan
Alta
Lander
Edmonton
B. C.
Victoria
Man
Vancouver
Winnipeg
N. B
Fredericton -.
N. S
Yarmouth
-12
26
Ont
London
P. E. I
Que..
Ottawa
-33
-51
-28
-27
-27
-34
-70
-68
7.5
13".~5
8.7
15.4
15.0
3.2
Pt. Arthur
Toronto
C harlotteto wn
Montreal.
Sask _
Quebec, ,.
Prince Albert
Yukon
Dawson
137
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
were arbitrarily chosen to increase the calculated heat loss on the side or
sides of the building exposed to the prevailing winds. It is also possible
to differentiate among the various exposures more accurately by calcu-
lating the infiltration and transmission losses separately for the different
sides of the building, using different assumed wind velocities. Recent
investigations indicate, however, that the wind direction indicated by
Weather Bureau instruments does not always correspond with the
direction of actual impact on the building walls, due to deflection by
surrounding buildings.
Pending the time when the lack of actual test data is remedied, it is
recommended that no differentiation be made among the various sides of
a building in calculating the heat losses. It should be remembered that
the values for U in the tables in Chapter 5 are based on a wind velocity
of 15 mph.
The Heating, Piping and Air Conditioning Contractors National Associ-
ation has devised a method2 for calculating the square feet of equivalent
direct radiation required in a building. This method makes use of ex-
posure factors which vary according to the geographical location and the
angular situation of the construction in question in reference to pre-
vailing winds and the velocity of them.
HEAT FROM SOURCES OTHER THAN HEATING PLANT
The heat supplied by persons, lights, motors and machinery should
always be ascertained in the case of theaters, assembly halls, and in-
dustrial plants, but allowances for such heat sources must be made only
after careful consideration of all local conditions. In many cases, ^ these
heat sources should not be allowed to affect the size of the installation at
all, although they may have a marked effect on the operation and con-
trol of the system. In general, it is safe to say that where audiences are
involved, the heating installation must have sufficient capacity to bring
the building up to the stipulated inside temperature before the audience
arrives. In industrial plants, quite a different condition exists, and heat
sources, if they are always available during the period of human occu-
pancy, may be substituted for a portion of the heating installation. In
no case should the actual heating installation (exclusive of heat sources)
be reduced below that required to maintain at least 40 F in the building.
Motors and Machinery
Motors and the machinery which they drive, if both are located in the
room, convert all of the electrical energy supplied into Jheat, which is
retained in the room if the product being manufactured is not removed
until its temperature is the same as the room temperature.
If power is transmitted to the machinery from the outside, then only
the heat equivalent of the brake horsepower supplied is used, In the
^ ,. ^ i Motor horsepower vxOC/,~ A
first case the Btu supplied per hour = Efficiency of motor X 2,546, and
in the second case Btu per hour = bhp X 2,546, in which 2,546 is the
Btu equivalent of 1 hp-hour. In high-powered mills this is the chief
2See Standards of Heating, Piping and Air Conditioning Contractors National Association.
138
CHAPTER 7 — HEATING LOAD
source of heating and it is frequently sufficient to overheat the building
even in zero weather, thus requiring cooling by ventilation the year
round.
The heat (in Btu per hour) from electric lamps is obtained by multi-
plying the watts per lamp by the number of lamps and by 3.415. One
cubic foot of producer gas gives off about 150 Btu per hour; one cubic
foot of illuminating gas gives off about 535 Btu per hour; and one cubic
foot of natural gas gives off about 1000 Btu per hour. A Welsbach
burner averages 3 cu ft of gas per hour and a fish-tail burner, 5 cu ft
per hour. For information concerning the heat supplied by persons,
see Chapter 2.
In intermittently heated buildings, besides the capacity necessary
to care for the normal heat loss which may be calculated according to
customary rules, additional capacity should be provided to supply the
heat necessary to warm up the cold material of the interior walls, floors,
and furnishings. Tests have shown that when a cold building has had its
temperature raised to about 60 F from an initial condition of about 0 F,
the heat absorbed from the air by the material in the structure may vary
from 50 per cent to 150 per cent of the normal heat loss of the building.
It is therefore necessary, in order to heat up a cold building within a
reasonable length of time, to provide such additional capacity. If the
interior material is cold when people enter a building, the radiation of
heat from the occupants to the cold material will be greater than is
normal and discomfort will result. (See Chapter 2.)
CONDENSATION ON BUILDING SURFACES3
Condensation on the interior surfaces of buildings is often a serious
problem. Water dripping from a ceiling may cause irreparable damage
to manufactured articles and machinery. It often results in short-cir-
cuiting of electric power and lighting systems, necessitating shut-downs
and incurring costly repairs. It also causes rotting of wood roof struc-
tures, corrosion of metal roofs, and spalling and disintegration of gypsum
and other types of roof decks not properly protected.
Condensation is caused by the contact of the warm humid air in a
building with surfaces below the dew-point temperature, and can be
remedied in two ways, (1) by increasing the temperature of such surfaces
above the dew-point temperature, or (2) by lowering the humidity.
Dehumidification, of course, is not advisable where a high relative
humidity is necessary for manufacturing processes. Hence, the^ only
alternative is to increase the surface temperature by decreasing the inside
surface resistance. This can be accomplished by increasing the velocity
of air passing over the surface, or by increasing the over-all Resistance of
the wall or roof by installing a sufficient thickness of insulation.
The latter method is generally used, and the thickness of insulation
is determined by ascertaining the amount of resistance to be added ^ to
increase the temperature of the interior surface above ^ the dew-point
temperature for the maximum conditions involved. This in turn is based
on the fundamental principle that the drop in temperature is proportional
to the resistance. See Question 1 at the end of this chapter.
2See Preventing Condensation on Interior Building Surfaces, by Paul D. Close (A.S.H.V.E. TRANS-
ACTIONS, Vol. 36, 1930).
139
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
EXAMPLE OF HEAT LOSS COMPUTATIONS
Window
Crack i\
If Bnclc
Wall, i'
Interior
Surface. -
Coo*- at each End.
f[ Buulfc -up fcoof \oq on 3" Concrete tZoof Deck.
\
go
m
i Lonqttudinoi Axis North $ S
1- — 15 Windows each
side +'-CfWidft
M-P
louth
Lenqth 120'- 0*
^
4
1
D<
I
«rt-Cra
^-L
BSJ 5* Stonfc Concr«fca on
fc> y Cinder Concrete
JT onDtrt^
r
Solid U
«xiDoo«
ij
FIG. 1. ELEVATION OF FACTORY BUILDING
1. LOCATION _ Philadelphia, Pa.
2. LOWEST OUTSIDE TEMPERATURE. (Table 2) — 6 F
3. BASE TEMPERATURE: In this example a design temperature 10 F above lowest
on record instead of 15 F is used. Hence the base temperature =
(- 6 -f 10) = + 4 F.
4. DIRECTION OF PREVAILING WIND (during Dec., Jan., Feb.) Northwest
5. BREATHING-LINE TEMPERATURE (5 ft from floor) 60 F
6. INSIDE AIR TEMPERATURE AT ROOF:
The air temperature just below roof is higher than at the breathing line.
Height of roof is 16 ft, or it is 16 — 5 = 11 ft above breathing line. Allowing
2 per cent per foot above 5 ft, or 2 X 11 =22 per cent, makes the tem-
perature of the air under the roof = 1.22 X 60 = 73.2 F.
7. INSIDE TEMPERATURE AT WALLS:
The air temperature at the mean height of the walls is greater than at
the breathing line. The mean height of the walls is 8 ft and allowing 2 per
cent per foot above 5 ft, the average mean temperature of the walls is
1.06 X 60 = 63.6 F. By similar assumptions and calculations, the mean
temperature of the glass will be found to be 64.2 F and that of the doors
61.2 F.
8. AVERAGE WIND VELOCITY (Table 2) 11.0 mph
9. OVER-ALL DIMENSIONS (See Fig. 1) 120 x 50 x 16 ft
10. CONSTRUCTION:
Walls — 12-in. brick, with H-in. plaster applied directly to inside surface.
Roof — 3-in. stone concrete and built-up roofing.
Floor — 5-in. stone concrete on 3-in. cinder concrete on dirt.
Doors— One 12 ft x 12 ft wood door (2 in. thick) at each end.
Windows — Fifteen, 9 ft x 4 ft single glass double-hung windows on each side.
11. TRANSMISSION COEFFICIENTS:
Walls— (Table 3, Chapters, WalI2B) U = 0.34
Roof— (Table 11, Chapter 5, Roofs 2A and 3A) U = 0.77
Floor— (Table 10, Chapter 5, Floors 5A and 6A) U = 0.63
Doors— (Table 13B, Chapters) U - 0.46
Windows— (Table 13A, Chapters) U = 1.13
140
CHAPTER 7 — HEATING LOAD
12. INFILTRATION COEFFICIENTS:
Windows — Average windows, non-weatherstripped, JlV"1- crack and
%4-in. clearance. The leakage per foot of crack for an 11-mile wind
velocity is 25.0 cfh. (Determined by interpolation of Table 2,
Chapter 6.) The heat equivalent per hour per degree per foot of
crack is taken from Chapter 6.
25.0 X 0.018 = 0.45 Btu per deg Fahr per foot of crack.
Doors — Assume infiltration loss through door crack twice that of windows
or 2 X 0.45 = 0.90 Btu per deg Fahr per foot of crack.
Walls — As shown by Table 1, Chapter 6, a plastered wall allows so little
infiltration that in this problem it may be neglected.
13. CALCULATIONS: See calculation sheet, Table 3.
TABLE 3.
CALCULATION SHEET SHOWING METHOD OF ESTIMATING HEAT LOSSES OF
BUILDING SHOWN IN FIG. 1
PART OF BUILDING
WIDTH
IN
FEET
HEIGHT
IN
FEET
NET SUR-
FACE AREA
OR CRACK
LENGTH
COEFFI-
CIENT
TEMP.
DIFF.
TOTAL
BTU
North Wall:
Brick, H-in- plaster
50
12
1 pair
16
12
doors
656
144
60
0.34
0.46
0.90
59.6
57.2
57.2
13,293
3,789
l,544a
Doors (2-in. wood)
\i in. Crack.__
West Wall:
Brick, H-in plaster
120
15x4
Double
Window
16
9
Hung
re (15)
1380
540
450
0.34
1.13
0.45
59.6
60.2
60.2
27,964
36,734
6,09 5a
Glass (Single)
% in. Crack.
South Wall _
Same as North Wall
18,626
East Wall
Same as West Wall
70.793
Roof, 3-in. concrete and slag-
surfaced built-up roofing
50
120
6000
0.77
69.2
319,704
Floor, -^-in. stone concrete on
3-in. cinder concrete „
50
120
6000
0.63
5b
18,900
GRAND TOTAL of heat required for building in Btu pei
" hour
517,442
"This building has no partitions and whatever air enters through the cracks on the windward side must
leave through the cracks on the leeward side. Therefore, only one-half of the total crack will be used in
computing infiltration for each side and each end of building.
bA 5 F temperature differential is commonly assumed to exist between the air on one side of a large
floor laid on the ground and the ground.
PROBLEMS IX PRACTICE
1 • The dry-bulb temperature and the relative humidity at the ceiling of a
mixing room in a bakery are 80 F and 60 per cent, respectively. The roof is a
4-in. concrete deck covered with built-up roofing. If the lowest outside tem-
perature to be expected is — 10 F, what thickness of rigid fiber insulation will be
required to prevent condensation?
From Table 11, Chapter 5, U for the uninsulated roof = 0.72. From Table 2, Chapter 5 ,
k for rigid fiber insulation == 0.33. From the psychrometric chart, Chapter 1, the dew
point of air at 80 F and 60 per cent relative humidity is 65 F. The ceiling temperature,
therefore, must not drop below 65 F if condensation is to be prevented.
141
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
When equilibrium is established, the amount of heat flowing through any component
part of a construction is the same for each square foot of area.
Therefore,
^7 [80 - (-10)] - 1.65 (80 - 65)
where
U is the transmittance of the insulated roof.
Solving the equation, U « 0.275.
The resistance of the insulated roof = n 0?, =3.64.
The resistance of the uninsulated roof = , 70 = 1.39.
U. 1 2i
The resistance of the insulation = 3.64 - 1.39 = 2.25.
Resistance per inch of insulation = A Q9 =3.0.
U.Oo
Since a resistance of 2.25 is required, and 1 in. of insulation has a resistance of 3, one inch
will be sufficient to prevent condensation.
The same result might have been obtained by selecting an insulated 4-in. concrete slab
having a U of less than 0.275 from Table 11, Chapter 5. This 4-in. concrete slab with
1-in. rigid insulation has a U of 0.23 which is safe.
2 • What inside dry -bulb temperatures are usually assumed for: (a) homes,
(b) schools, (c) public buildings?
Referring to Table 1 :
a. 70 to 72 F.
b. Temperature varies from 55 to 75 F, depending on the room. Classrooms, for instance,
are usually specified as 70 to 72 F.
c. 68 to 72 F.
3 • How is the outside temperature selected for use in computing heat losses?
The outside temperature used in computing heat losses is generally taken from 10 to 15 F
higher than the lowest recorded temperature as reported by the Weather Bureau during
the preceding 10 years for the locality in which the heating system is to be installed.
In some cases where the lowest recorded temperature is extremely unusual, the design
temperature is taken even higher than 15 F above the lowest recorded temperature.
4 • What are the effects of wind movement on the heating load?
a. Wind movement increases the heat transmission of walls, glass, and roof; it affects
poor walls to a much greater extent than good walls.
b. Wind movement materially increases the infiltration (inleakage) of cold air through
the cracks around doors and windows, and even through the building materials them-
selves if such materials are at all porous.
5 • Calculate the heat given off by eighteen 200-watt lamps.
200 X 18 X 3.415 = 12,294 Btu per hour.
6 • A two-story, six room, frame house, 28-ft by 30-ft foundation, has the
following proportions:
Area of outside walls, 1992 sq ft.
Area of glass, 333 sq ft.
Area of outside floors, 54 sq ft.
Cracks around windows, 440 ft.
Cracks around doors, 54 ft.
Area of second floor ceiling, 783 sq ft.
Volume, first and second floors, 13,010 cu ft.
Ceilings, 9 ft high.
142
CHAPTER 7 — HEATING LOAD
The minimum temperature for the heating season is — 34 F, and the required
inside temperature at the 30-in. level is 70 F. The average number of degree
days for a heating season is 7851, and the average wind velocity is 10 mph,
northwest.
The walls are constructed of 2-in. by 4-in. studs -with wood sheathing, building
paper, and wood siding on the outside, and wood lath and plaster on the inside.
Windows are single glass, double-hung, wood, without weatherstrips. The
second floor ceiling is metal lath and plaster, without an attic floor. The roof
is of wood shingles on wood strips with rafters exposed. The area of the roof is
20 per cent greater than the area of the ceiling. Select values for the following:
(a) U for walls; (b) U for glass; (c) U for second floor ceiling; (d) U for roof;
(e) U for ceiling and roof combined; (f) air leakage, cubic feet per hour per foot
of window crack; (g) air leakage, cubic feet per hour per foot of door crack.
a. 0.25 (Table 5, Chapter 5).
b. 1.13 (Table 13, Chapter 5).
c. 0.69 (Table 8, Chapter 5).
d. 0.48 (Table 12, Chapter 5).
e. 0.236 (Equation 6, Chapter 5).
/. 21.4 (Table 2, Chapter 6).
g. 42.8, which is double the window leakage,
7 • Using the data of Question 6, calculate the maximum Btu loss per hour for
the various constructions, and show the percentage of the total heat which is
lost through each construction described.
Assume 2 per cent rise in temperature for each foot in height. The average temperature
will be 72.8 F for walls, doors, and windows, and 79.1 F for the second floor ceiling.
a. Outside walls 46,200 Btu loss 37.2 per cent of total
b. Glass 34,950 Btu loss 28.1 per cent of total
c. Doors 5,670 Btu loss 4.6 per cent of total
d. Second floor ceiling 17,840 Btu loss 14.3 per cent of total
e. Air leakage, windows 15,750 Btu loss 12.7 per cent of total
/. Air leakage, doors 3,865 Btu loss 3.1 per cent of total
Total 124,275 Btu loss 100.0 per cent of total
8 • For the house in Question 6, place 1-in. insulation in the outside walls and
second floor ceiling; k for insulation = 0.34. Use weatherstrip on doors and
windows, and double glass on the windows; Ca = 0.55. Calculate or select the
following values: (a) U for walls; (b) U for glass; (c) U for second floor ceiling;
(d) U for combination of ceiling and roof; (e) Air leakage, cubic feet per hour
per foot of door crack; (f) air leakage, cubic feet per hour per foot of window
crack.
a. 0.144.
b. 0.55.
c. 0.23.
d. 0.13.
e. 15.5.
/. 31.0.
9 • Calculate the maximum Btu loss per hour and show the percentage loss by
each channel for the house as insulated in Question 8.
a. Outside walls 26,650 Btu loss 36.2 per cent of total
b. Glass 17,000 Btu loss 23.1 per cent of total
c. Doors 5,670 Btu loss 7.7 per cent of total
d. Ceiling 10,070 Btu loss 13.7 per cent of total
e. Air leakage, windows 11,400 Btu loss 15.5 per cent of total
/. Air leakage, doors 2,795 Btu loss 3.8 per cent of total
Total 73,585 Btu loss 100.0 per cent of total
143
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
10 • From the results of Questions 7 and 9, calculate the Btu saved and the
percentage saved by each change in construction.
Insulated Uninsulated Btu Saved Per Cent Saved
a. Outside walls 46,200 26,650 19,550 42.3
b. Glass 34,950 17,000 17,950 51.4
c. Doors 5,670 5,670 0 0
d. Ceiling 3,865 2,795 1,070 27.7
e. Air leakage, windows 17,840 10,070 7,700 43.1
/. Air leakage, doors 15,750 11,400 4,350 27.6
11 • From the results of Questions 7 and 9, calculate the heat loads per heating
season in Btu and note the savings by better construction.
The 7851 degree days for the heating season multiplied by 24 hours, times the Btu loss
per hour for 1 F drop in temperature gives the Btu load per heating season.
Saving = 250,800,000 - 148,000,000 = 102,800,000 Btu.
Chapter 8
COOLING LOAD
Conditions to be Maintained, Cooling Load, Transmission for
Surfaces not Exposed to the Sun, Outside Temperatures, Solar
Radiation, Time Lag, Transmission of Solar Radiation Through
Glass, Heat and Moisture Leakage, Heat and Moisture Sources
THE method of calculating the cooling load is similar to that used
in calculating the heating load. The direction of the flow of heat is
reversed, however, and in most cases additional factors must be con-
sidered, such as solar radiation and the heat from occupants, lights,
motors, and other sources. The character of the load depends on the type
of building to be cooled as, for example, in auditoriums and other places
of assemblage where the maximum load usually is that due to the heat and
moisture given off by the occupants, or in office buildings and residences
where solar radiation and the transmission and infiltration of heat
through the building shell are most important.
While cooling is generally identified with the summer season, it is often
necessary to cool in winter as well as in summer. In a crowded place of
assemblage the heat given off by the occupants, together with that given
off by the lighting and power equipment, may be more than the normal
heat loss through the structure even in winter under cold climatic con-
ditions.
Much of the basic information for the design of comfort conditioning
installations has resulted from research conducted at the A.S.H.V.E.
Research Laboratory and at institutions with which cooperative research
investigations have been carried on. These data include the effective
temperature index, and heat and moisture loss data given in Chapter 2.
COMFORT CONDITIONS
The conditions to be maintained in an enclosure are variable and
depend on many factors, especially the season of the year and (during the
summer) the outside dry-bulb temperature and the duration of the period
of occupancy. Information concerning the proper effective temperatures
to be maintained for various seasons is given in Chapter 2, where are also
tabulated the most desirable indoor air conditions to be maintained in
summer for exposures less than three hours. (See Table 2, Chapter 2.)
In installations for restaurants and theaters the requirements are
different from those in offices, since there must be a considerable volume
of air circulated in order to provide ventilation and cooling.
145
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 1. AVERAGE MAXIMUM DESIGN DRY-BULB TEMPERATURES, DESIGN WET-BULB
TEMPERATURES, WIND VELOCITIES, AND WIND DIRECTIONS FOR
JUNE, JULY, AUGUST, AND SEPTEMBER
STATE
CITY
AVERAGE
MAXIMUM
DESIGN
DRY-BULB
DESIGN
WET-BULB
SUMMER WIND
VELOCITY
MPH
PREVAILING
SUMMER WIND
DIRECTION
Ala
Birmingham.
93
77
5.2
s
Mobile.
94
78
8.6
sw
Ariz
Phoenix.
HO
77'
6.0
WT
Ark
Little Rock.
95
77
7.0
NE
Calif
Los Angeles -
88
70
6.0
SW
San Francisco
85
68
11.0
sw
Colo
Denver
90
64
6.8
s
Conn
New Haven
88
74
7.3
s
D C
Washington
95
78
6.2
s
Fla
Jacksonville
94
78
8.7
sw
Tampa. _
94
79
7.0
E
Ga.
Atlanta
91
75
7.3
NW
Savannah
95
79
7.8
SW
Idaho
Boise
95
65
5.8
NW
111.
Chicago
95
75
10.2
NE
Peoria
91
75
8.2
S
Ind.
Indianapolis
90
73
9.0
SW
Iowa
Des Moines -
92
74
6.6
sw
Ky.
Louisville..
94
75
8.0
sw
La
New Orleans
94
79
7.0
sw
Maine.
Portland
85
71
7.3
s
Md
Baltimore
93
76
6.9
sw
Mass.
Boston
88
73
9.2
sw
Mich
Detroit .
93
73
10.3
sw
Minn.
Minneapolis
84
72
8.4
SE
IVOss
Vicksburg
95
78
6.2
sw
Mo.
Kansas City.
92
75
9.5
s
St. Louis .
95
78
9.4
sw
Mont.
Helena
87
63
7.3
sw
Nebr
Lincoln . .
93
74
9.3
s
Nev
Reno
93
64
7.4
w
N, J.
Trenton
95
76
10.0
sw
N. Y. ..
Albany
90
74
7.1
s
Buffalo. ...
83
72
12.2
sw
New York.....
95
75
12.9
sw
N. M
Santa Fe..
87
63
6.5
SE
N. C
Asheville
87
72
5.6
SE
Wilmington
93
79
7.8
sw
N Dak
Bismarck.
88
69
8.8
NW
Ohio
Cleveland.. . .
95
73
9.9
S
Cincinnati.
95
78
6.6
sw
Okla.
Oklahoma City
96
76
10.1
s
Oreg
Portland
83
65
6.6
NW
Pa.
Philadelphia
95
78
9.7
SW
Pittsburgh
91
73
9.0
NW
R. I.
Providence -.
85
73
10.0
NW
S. C.
Charleston
94
80
9.9
SW
Greenville.
93
76
6.8
NE
Tenn
Chattanooga
94
76
6.5
SW
Memphis .. .
93
77
7.5
sw
146
CHAPTER 8 — COOLING LOAD
TABLE 1. AVERAGE MAXIMUM DESIGN DRY-BULB TEMPERATURES, DESIGN WET-BULB
TEMPERATURES, WIND VELOCITIES, AND WIND DIRECTIONS FOR
JUNE, JULY, AUGUST, AND SEPTEMBER (Continued)
STATE
CITY
AVERAGE
MASSMUM
DESIGN
DRY-BULB
DESIGN
WET-BULB
SUMMER WIND
VELOCITY
MPH
PREVAILING
SUMMER WIND
DIRECTION
Texas
Dallas
99
76
94
s
Galveston
93
79
97
s
San Antonio
100
78
74
SE
Houston
93
79
7.7
s
El Paso
98
69
69
E
Utah
Salt Lake City
95
67
8.2
SE
Vt
Burlington
85
71
89
s
Va.
Norfolk
91
76
10.9
s
Richmond
95
78
62
SW
Wash
Seattle
83
61
79
s
Spokane
89
63
6 5
SW
WT Va
Parkersburg
90
74
5 3
SE
Wis.
Madison
89
73
8 1
SW
Milwaukee
93
74
10.4
s
Wyo.
y
Cheyenne
85
62
92
S
COOLING LOAD
The cooling load may be divided into the following parts:
1. Transmission of heat through walls, roof, and glass with allowances for sun-
exposed surfaces and heat capacity.
2. Transmission of solar radiation through glass and absorption by interior furnishings.
3. Heat and moisture from infiltration and from outside air introduced.
4. Heat and moisture from occupants and heat from lights, machinery and other
sources.
Transmission for Surfaces Not Exposed to the Sun
The transmission load for surfaces not exposed to the sun is calculated in
a manner similar to that described in Chapter 7, by means of the following
formula:
Ht = AU(to-t) (1)
where
Ht = heat transmitted through the material of the wall, glass, roof, or floor, Btu
per hour.
A = net inside area of wall, glass, roof, or floor, square feet.
t — inside temperature, degrees Fahrenheit.
to = outside temperature, degrees Fahrenheit.
U — coefficient of transmission of wall, floor, roof, or glass, Btu per hour per
square foot per degree Fahrenheit difference in temperature. (Tables 3 to 13,
Chapter 5.)
Outside Temperatures
Summer dry-bulb and wet-bulb temperatures for various -cities are
given in Table 1. It will be noted that the temperatures are not the
maximums but the design temperatures which should be used in air-
conditioning calculations. The maximum outside wet-bulb temperatures
147
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
as given in Weather Bureau reports usually occur only from 1 per cent to
4 per cent of the time, and they are therefore of such short duration that
it is not practical to design a cooling system covering this range. The
temperatures shown in Table 1 have been chosen after extensive study of
the Weather Bureau records and are temperatures that are not exceeded
more than 5 to 8 per cent of the time during June, July, August, and
September for an average year.
Solar Radiation
Fig. 1 shows the total amount of solar energy in Btu per square foot per
hour received during the day by a surface normal to the rays of the sun,
by a horizontal surface, and by east, west, and south walls. The curves
are drawn from A.S.H.V.E. Laboratory data obtained by pyrheliometer,
are based on sun time, and are for a perfectly clear day on August 1 at a
north latitude of 40 deg. Data from these curves may be used with
little error for most United States latitudes and for all of the hotter
months of the year.
The absorption of solar radiation by a surface depends upon the
character of the surface and the angle of the surface with respect to the
direction of the radiation. The heat absorption by a black oilcloth
surface perpendicular to the sun's rays was found to be as high as 273 Btu
per square foot per hour, based on tests conducted by the A.S.H.V.E.
Research Laboratory in Pittsburgh1. Lamp black, red brick dust, and
aluminum bronze painted surfaces perpendicular to the sun's rays
showed, respectively, 94.0, 63.4, and 28.2 per cent as high a rate of
absorption as the black oilcloth.
TABLE 2. ALLOWANCE FOR SOLAR RADIATION ON ROOFS AND WALLS
APPROXIMATE NUMBER OF DEGREES TO ADD TO DRY- BULB TEMPERATURE
FOR DIFFERENT TYPES OF SURFACES
TYPE OF SURFACE
BLACK
RED BRICK OR TILE
ALTTMINUM PA. INT
Roof horizontal
45
30
15
East or west wall
30
20
10
South wall -
15
10
5
Solar radiation is an important factor in the mechanism of heat flow
into buildings. Research conducted at the A.S.H.V.E. Research Labora-
tory2 has shown that a large error may be introduced into the calculations
by failure to consider the periodical character of heat flow resulting from
the diurnal movement of the sun and the heat capacity of the structure,
which determine the timing and magnitude of the heat wave flowing
through the wall into a building on a hot, sunny day.
Absorption of Solar Radiation in Relation to the Temperature, Color, Angle, and Other Characteristics
of the Absorbing Surface, by F. C. Houghten and Carl Gutberlet (A.S.H.V.E. TRANSACTIONS, Vol. 36, 1930),
2For further information on this subject see following A.S.H.V.E. research papers: Coefficients of Heat
Transfer as Measured under Natural Weather Conditions, by F. C. Houghten and C. G. F. Zobel (A.S.H.
V.E. TRANSACTIONS, Vol. 34, 1928); Absorption of Solar Radiation in Its Relation to the Temperature,
Color, Angle and Other Characteristics of the Absorbing Surface, by F. C. Houghten and Carl Gutberlet
(A.S.H.V.E. TRANSACTIONS, Vol. 36, 1930); Heat Transmission as Influenced by Heat Capacity and Solar
Radiation, by F. C. Houghten, j. L. Blackshaw, E. M. Pugh and Paul McDermott (A.S.H.V.E. TRANS-
ACTIONS, Vol. 38, 1932).
148
CHAPTER 8 — COOLING LOAD
Unfortunately, the calculations for the transmission of heat from solar
radiation through building walls are too complicated to be of much
practical value to the heating and ventilating engineer. Approximate
results may be obtained by adding the number of degrees given in Table 2
to the outside design dry-bulb temperature in calculating the heat trans-
mission through a wall or roof which may be exposed to the sun for an
appreciable length of time. Table 2 was obtained from a study of the
data in A.S.H.V.E. research papers on solar radiation1' 3. Black and
aluminum painted surfaces represent the extremes which are likely to
occur. For other types of surfaces, values intermediate between those
given in the table can be used.
Time Lag
The calculation of heat transmitted through walls and roofs does not
take into consideration the heat capacity of the structure and the con-
sequent time lag in the transmission of heat. In the thick walls used in
modern office buildings the time lag may amount to 10 hours or more4.
Thus in many cases the wall transmission cannot be added directly to the
cooling load from other sources because the peak of the wall transmission
load may not coincide with the peak of the total cooling load and may
even occur after the cooling system has been shut down for the day. The
data in Table 3 were taken from A.S.H.V.E. research papers3' 4 and
while they result principally from a study of experimental slabs, they give
an idea of the time lag to be expected in various structures.
TABLE 3. TIME LAG IN TRANSMISSION OF SOLAR RADIATION THROUGH WALLS AND ROOFS
TYPE AND THICKNESS OP WALL OR ROOF
TIME LAG,
HOTTRS
2-in. pine - _
6-in. concrete
4-in. gypsum
3-in. concrete and 1-in. cork..
2-in. iron and cork (equivalent to %-in. concrete and 2.15-in. cork)...
4-in. iron and cork (equivalent to 5j^-in. concrete and 1.94-in. cork)..
8-in. iron and cork (equivalent to 16-in. concrete and 1.53-in. cork)..
19
22-in. brick and tile wall _._.j 10
In intermittently cooled buildings an excess cooling capacity must be
provided to care for the additional load imposed by the necessity to cool
down the furnishings and the material of the interior construction to the
point of maintained temperatures.
Transmission of Solar Radiation Through Glass
In considering the transmission through glass several factors must be
considered. As the sun's rays impinge against a pane of glass, most of the
radiation passes through to the other side, a small amount is reflected, and
the balance is absorbed by the glass. The amount absorbed depends upon
'Heat Transmission as Influenced by Heat Capacity and Solar Radiation, by F. C. Houghten, J. L.
Blacksnaw, E. M. Pugh, and Paul McDermott (A.S.H.V.E. TRANSACTIONS, Vol. 38, 1932).
'Field Studies of Office Building Cooling (A.S.H.V.E. Research Paper), by J. H. Walker, S. S. Sanford,
and E. P. Wells (A.S.H.V.E. TRANSACTIONS, Vol. 38, 1932).
149
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 193-5
rue
CHAPTER 8 — COOLING LOAD
the character and thickness of the glass and the angle between the rays of
sunlight and the glass. The temperature of the glass is raised by the
absorbed heat and this heat is then delivered to the air on the two sides of
the glass in proportion to the difference between glass and air tem-
peratures.
The A.S.H.V.E. tests indicated that a single pane of double strength
glass 0.127 in. thick absorbs approximately 11 per cent of the solar
radiation passing through it when the impingement is normal. For
smaller angles of impingement, the glass retards percentages of the total
radiant energy approximately in proportion to the sine of the angle.
Other experiments4 indicate a glass absorption of 16.7 per cent for one
pane of glass and 37.5 per cent for two J^-in. panes separated by a 1%-in.
air space.
The amount of solar radiation delivered to an unshaded glass surface
may be obtained from the curves in Fig. 1. For surfaces other than those
given, the solar radiation incident to the glass must be calculated.
Hendrickson and Walker6 have shown how this may be done if the wall
faces some direction other than east, west, or south. They have also
shown how to calculate the net glass area on which the solar radiation
impinges when the glass is partly shaded by the frame or wall. The
values from Fig. 1 must be used only for the net glass area on which the
sun shines. Recent tests at the A.S.H.V.E. Research Laboratory6 have
determined the percentage of heat from solar radiation actually delivered
to a room with bare windows and with various types of outdoor and
indoor shading. The data in Table 4 are taken from these tests.
TABLE 4. SOLAR RADIATION TRANSMITTED THROUGH BARE AND SHADED WINDOWS
PER CENT DELIVERED
TO ROOM
Bare window glass
97
Canvas awning . ....
28
Inside shade," fully drawn
45
Inside shade, one-half drawn
68
Inside Venetian blind, fully covering window
58
Outside Venetian blind, fully covering window
22
The percentage figures in this table were obtained by dividing the total
amount of heat actually entering through the shaded window by the
total amount of heat calculated to enter through a bare window (solar
radiation plus glass transmission based on observed outside glass tem-
perature). For bare windows on which the sun shines, the transmission
of heat from outside air to glass is small as the glass temperature is raised
by the solar radiation absorbed. Therefore, in calculating the total heat
gain through windows on the sunny sides of buildings, it is sufficiently
accurate to figure the total cooling load due to the window, as the solar
radiation times the proper factor from Table 4, and to neglect the heat
*Summer Cooling for Comfort as Affected by Solar Radiation, by G. A. Hendrickson and ]. H. Walker,
Heating and Ventilating, November, 1932, and The Determination of Sun Effect on Summer Cooling Loads,
by G. A. Hendrickson and J. H. Walker, Heating and Ventilating, June, 1933.
^Studies of Solar Radiation Through Bare and Shaded Windows, by F. C. Houghten, Carl Gutberlet,
and J. L. Blackshaw (A.S.H.V.E, Journal Section, Heating, Piping and Air Conditioning, February, 1934).
151
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
transmission through the glass caused by the difference between the
temperatures of the inside and outside air. Another reason for neglecting
this glass transmission load is that the curves in Fig. 1 were based on the
maximum intensity of solar radiation observed at the A.S.H.V.E. Labora-
tory during a three-year study, so results based on these curves will be
amply high. It will be noted that Table 4 gives the amount of heat
delivered through the window as 97 per cent of the solar radiation, which
is greater than is indicated by the figures for absorption in the preceding
paragraph. The explanation is that much of the radiation absorbed by
the glass is delivered to the room.
Fig. 1 shows that the maximum solar intensity on any surface is of
limited duration. In the case of windows the total energy impinging on
the glass before and after the time of maximum intensity is further
reduced by increased shading of the glass from the frame, or wall. The
cooling load due to solar radiation therefore does not have to be figured as
a steady load. Another point which should be noted is that the maximum
solar radiation load on an east wall occurs early in the morning when the
outside temperature is low.
In a recent paper by the A.S.H.V.E. Research Laboratory7 it was shown
that ordinary double strength window glass transmits no measurable
amount of energy radiated from a source at 500 F or lower ; that it trans-
mits only 6.0 and 12.3 per cent of the total radiation from surfaces at
700 F and 1000 F, respectively; and that it transmits 65.7 per cent of the
radiation from an arc lamp, 76.3 per cent of the radiation from an in-
candescent tungsten lamp, and 89.9 per cent of the radiation from the
sun. Thus, glass windows in a room constitute heat traps, which allow
rather free transmission of radiant energy into the room from the sun to
warm objects in it, but do not allow the transmission of re-radiated heat
from these same objects.
Some recent tests4 indicated that sunshine through window glass is
the most important factor to contend with in the cooling of an office
building. At times it was shown to account for as much as 75 per cent of
the total cooling necessary. Because of the importance of the sunshine
load, cooling systems should be zoned so that the side of the building on
which the sun is shining can be controlled separately from the other sides
of the building. If buildings are provided with awnings so that the
window glass is shielded from sunshine, the amount of cooling required
will be reduced and there will also be less difference in the cooling require-
ments of different sides of the building. The total cooling load for a
building exposed to the sun on more than one side is of course less than
the sum of the maximum cooling loads in the individual rooms since the
maximum solar radiation load on the different sides occurs at different
times.
Heat and Moisture Leakage
An allowance must be made for the heat and moisture in the outside air
introduced for ventilating purposes or entering the building through
cracks, crevices, doors, and other places where infiltration might occur.
'Radiation of Energy Through Glass, by J. L. Blackshaw and F. C. Houghten (A.S.H.V.E. Journal
Section, Heating, Piping and Air Conditioning, October, 1933).
152
CHAPTER 8 — COOLING LOAD
The volume of air entering due to infiltration may be estimated from data
given in Chapter 6, and information on the amount of outside air required
for ventilation will be found in Chapter 2.
The heat gain resulting from the outside air introduced may be esti-
mated from the following formula:
Hi = Qd0 (00 - 0) (2)
where
Hi = heat to be removed from outside air entering the building, Btu per hour.
Q — volume of outside air entering the building, cubic feet per hour.
d0 = density of outside air, pounds of dry air per cubic foot of outside air, at the
temperature A>
©o ~ heat content of mixture of outside dry air (at temperature to) and water vapor,
Btu per pound of dry air.
© = heat content of mixture of inside dry air (at temperature /) and water vapor,
Btu per pound of dry air.
Heat and Moisture Sources
Figs. 6 to 9, Chapter 2, show the heat and moisture given off by human
beings under various conditions of activity. For average conditions where
a person is normally at rest, as in a theater, or doing very light work, as in
a restaurant or residence, the total amount of heat given off will average
about 400 Btu per hour. Part of this is latent heat due to the evaporation
of 700 to 1200 grains of moisture per hour. Examples illustrating heat and
moisture loss calculations for human beings are given in Chapter 2.
TABLE 5. HEAT GAIN DUE TO VARIOUS DEVICES, BTU PER HOUR
Lights and electric appliances
3,415 per kilowatt
Motors, X-JLO hp
255
Motors, 1 hp
2,546
Restaurant coffee urns, 10-gal capacity
16",000
Dish warmers per 10 sq ft of shelf
6,000
Restaurant range — 4 burners and oven
100,000
Residence gas range
Giant burner
12,000
Medium burner
9,000
Oven
1,000 per cu ft of space
Pilot.. ..
250
Electric Range
Small burner, 100 to 1350 watts
3,415 to 4,600
Large burner, 1700 to 2200 watts
5,800 to 7,500
Oven, 2000 to 3000 watts
6,830 to 10,245
Appliance connection, 660 watts
2,250
Warming compartment, 300 watts
1.025
All sources of heat must of course be considered in designing the con-
ditioning system. The heat gain due to various devices is given in
Table 5. An example of cooling load calculation is given in Chapter 9.
PROBLEMS IN PRACTICE
1 • a. What should be the dry- and wet-bulb temperatures in a restaurant
when the outdoor dry-bulb temperature is 95 F?
b. "What is the most desirable indoor dry -bulb temperature and relative
humidity in an office building in summer?
a. Dry-bulb, 80 F; wet-bulb, 65 F. (Table 2, Chapter 2.)
b. 76.5 F and 50 per cent relative humidity. (Fig. 3, Chapter 2.)
153
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
2 • The outdoor and indoor temperatures are 90 F and 78 F, respectively.
What is the amount of heat transmitted per hour through a 7 ft by 4 ft north
window?
Ht = 28 X 1.13 (90- 78) = 380 Btu per hour.
(Equation 1, Chapter 8 and Table 12, Chapter 5.)
3 • What are the proper design temperatures for a Detroit store?
Outdoor dry-bulb, 88 F; wet-bulb, 72 F. (Table 1, Chapter 8.)
Indoor dry-bulb, 77.5 F; wet-bulb, 64.5 F. (Table 2, Chapter 2.)
4 • a. What is the maximum heat transmission for a flat roof exposed to the
sun with the outdoor and indoor temperature 95 F and 80 F, respectively? The
roof is of uninsulated 6-in. concrete, with its underside exposed, and with a
black upper surface.
b. If the temperatures specified were the maximum for the day and occured
at 12 o'clock, at what time would the maximum cooling load due to the roof
exist?
a. Ht = 1 X 0.64 (95 + 45 - 80) » 38.4 Btu per hour per square foot.
(Equation 1 and Table 2, Chapter 8, and Table 11, Chapter 5.)
b. At 3 p.m. (Table 3.)
5 • For south windows equipped with canvas awnings, what is the maximum
amount of heat delivered to a room when the outdoor temperature is 90 F and
the indoor temperature is 78 F?
115 X 0.28 = 32.2 Btu per square foot of glass (Fig. 1 and Table 4; note that glass
transmission can be neglected).
6 • What is the heat gain per cubic foot of outside air introduced, under the
following conditions :
Outdoor temperatures, 90 F dry-bulb and 75 F wet-bulb.
Inside temperatures, 78 F dry-bulb and 65 F wet -bulb.
Hi = Qdo (©o - ©). Equation 2.
The relative humidity of the outdoor air is 50 per cent (Fig. 3, Chapter 2), and d0 —
I
14.21
= 0.0703 (Table 5, Chapter 1).
© « 37.81 and © = 29.65 (Table 5, Chapter 1). The total heat of any air- vapor mix-
ture may be obtained from the last column in Table 5, Chapter 1, by considering the
temperatures to be wet-bulb readings, since the total heat of a mixture is constant for a
given wet-bulb temperature.
Hi = 1 X 0.0703 (37.81 - 29.65) = 0.57 Btu per cu ft.
7 • If there are twenty 200 -watt lights in use in a room, what is the cooling
load due to lights?
200 X 20 » 4000 watts = 4 kw.
3415 X 4 = 13,660 Btu per hour (Table 5, Chapter 8).
8 • a. When a restaurant has two 10-gal coffee urns, what is the cooling load
due to them?
b. What is the cooling load due to four 1350 -watt burners on an elecjtric
range?
a. 16,000 X 2 « 32,000 Btu per hour (Table 5, Chapter 8).
b. 4600 X 4 = 18,400 Btu per hour (Table 5, Chapter 8).
154
Chapter 9
CENTRAL AIR CONDITIONING
SYSTEMS
Types of Systems, Dehumidifier s, Designing the System, Zoning,
Location of Apparatus, Temperature of the Air Leaving Outlets,
Air Quantity Required, Heat to be Removed by Cooling and
Dehumidifying Apparatus, Size of Reheaters, Surface Cooling
Problems, Auxiliary Equipment
systems, equipped for cooling and dehumidifying, are used
_ principally in the air conditioning of theaters, restaurants, office
buildings, or other places where many people gather, and in manufacturing
establishments where air conditions have an important influence on the
quality of product or rate of production. A central cooling and de-
humidifying plant is one in which the fans, dehumidifiers, and other
related apparatus are assembled in suitable apparatus rooms from which
distribution and return ducts lead to the conditioned spaces. The design
of such systems is considered in this chapter, while in Chapter 22 central
systems for heating and humidifying are described. Industrial air con-
ditioning has been considered in Chapter 3.
TYPES OF SYSTEMS
Dehumidification or cooling of air may be accomplished by several
methods and by use of many heat transfer mediums. Most comfort-
conditioning, central station, air-conditioning systems employ cold water
or the direct expansion of a refrigerant in either spray type or surface
type equipment to accomplish the required cooling and dehumidification.
Among the several other methods that may be employed are : passing the
air through or over a dehydrating agent and then lowering the dry-bulb
temperature to the proper level, and evaporative cooling. The former
method is applicable to comfort conditioning only where reasonably cold
water is available for reducing the dry-bulb temperature after dehydra-
tion, while the latter method is applicable to comfort conditioning only in
regions where the summer wet-bulb temperature is low.
If the system is intended solely for summer conditioning, the apparatus
will consist essentially of a dehumidifier of the surface type or spray type ;
filters; fan and motor; reheater; outside air, return air, and supply air duct
work; air outlets and grilles; spray pump for spray dehumidifier; refrigera-
tion equipment; and suitable controls. Generally, however, a central
station air conditioning system is designed for year-round service. This
means that properly sized heaters and humidifiers, with their respective
155
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
controls, must be added. With few exceptions, systems designed to meet
summer capacity requirements will have ample capacity for winter and
intermediate season conditioning.
A common arrangement of a central station spray type system for
cooling and dehumidifying is illustrated in Fig. 1. The plant may be
designed to condition 100 per cent outside air, 100 per cent return air,'or a
mixture of outside and return air. Further, part of the air returned from
the conditioned space may be by-passed1 around the conditioner as
illustrated in Fig. 2. The reheater may be installed in the fan inlet
chamber as shown, in the by-pass air duct, or in the fan discharge duct,
depending upon apparatus space and other design conditions. Still
another arrangement of equipment will result if the dehumidified air fan
delivers the conditioned air to several other fans rather than to the con-
Outside
FIG. 1. SPRAY TYPE AIR CONDITIONING APPARATUS
ditioned space directly. These booster fan equipments may use part by-
pass air as illustrated in Fig. 3 or 100 per cent dehumidified air and
reheaters. The main apparatus, in either case, may or may not have a
by-pass connection, depending on load conditions and other design factors.
The systems illustrated in Figs. 1 and 2 may be converted into the
surface cooling type by merely replacing the dehumidifiers with surface
cooling coils which use cold water or direct expansion of refrigerant to
accomplish the required cooling and dehumidifying. The coils may also
be installed within the spray chamber, either in series with the sprays
or below them.
DEHUMIDIFIERS
Information on spray type dehumidifiers is given in Chapter 11.
Surface cooling type dehumidifiers generally consist of extended-surface
coils within which the water or refrigerant is circulated or the refrigerant
is expanded. The air to be cooled and dehumidified is drawn or blown
over the coils. This system is generally comparatively low in initial cost
and has low operating costs. For comfort cooling, water is usually used to
Patents exist covering the use of the by-pass for cooling and dehumidifying systems.
156
CHAPTER 9 — CENTRAL AIR CONDITIONING SYSTEMS
bring the refrigeration effect to the coils. Many localities have refrigera-
tion codes which restrict the use, in comfort conditioning applications, of
refrigerants acting by direct expansion in coils exposed to the air stream.
Therefore, local codes should be consulted by the designer before he plans
a system employing direct-expansion methods. Close humidity control
cannot be maintained during the cooling season by the surface cooling
type of equipment. Winter humidification may be accomplished by use
of evaporating pans or spray nozzles. The cooling coils serve no purpose
during the intermediate or heating seasons, so in this respect the spray
type equipment is often preferred, in that during certain seasons evapora-
tive cooling will be sufficient to produce the cooling desired. Effective
cooling and dehumidification accomplished by surface units are dependent
upon many variable factors. The air velocity through the unit, air
FIG. 2. SPRAY TYPE AIR CONDITIONING APPARATUS WITH BY- PASS
temperature, moisture content of the air, water or refrigerant tempera-
ture, and velocity of the water or refrigerant through the tubes must be
considered in selecting the proper unit for a given design load. If any of
these factors vary without a corresponding variation of the other factors,
the effective work of the coil will increase or decrease, as the case may be.
DESIGNING THE SYSTEM
The general procedure for the design of a central cooling and de-
hum Jdifying system is as follows :
1. Calculate the heat gain for each room or space to be conditioned. (See Chapters
5 and 8.)
2. Determine the volume of outside air to be introduced. (See Chapter 2.)
3. Assume or calculate the temperature of air leaving the supply outlets.
Calculate the quantity of air to be circulated.
Estimate the temperature loss in the duct system.
Calculate the heat to be removed by the cooling and dehumidifying apparatus.
Calculate the size of the reheating equipment.
8. Select cooling equipment and heating equipment from manufacturers' data and
performance curves.
9. Calculate total tonnage.
157
4.
5.
6.
7.
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
10. Design the air distribution system and the air outlets and inlets. (See Chapters
19 and 20.)
11. Calculate the total static pressure of the system.
12. Select the fan, motor, and drive. (See Chapter 17.)
13. Select the pump and motor.
14. Design the control system. (See Chapter 14.)
ZONING
The above general outline of procedure will prove satisfactory for the
smaller and less complex installations. However, when dealing with air-
conditioning systems for large buildings, after a proper analysis has been
made of the conditions to be maintained and the heat loads encountered,
it is generally considered best practice to divide the complete job into a
Motor
t°
t
s
ggg ,
|Fanl | I To room B •
FIG. 3. CENTRAL DEHUMIDIFYING PLANT AND LOCAL RECIRCULATING FANS
number of suitably sized units. In some cases a unit per floor or group of
floors may complete the design satisfactorily, whereas in others it may be
advantageous to have separate units for each of the various outside
exposures of the building. Where the floor area is large in relation to the
outside wall exposure, it is obvious that provision must be made for the
variable load to which the outside exposures are subjected. The heat
loads on inside rooms are apt to be less variable since the fluctuations of
the outside weather conditions are not directly involved. Such conditions
often result in the natural zoning or segregation of rooms having similar
exposures and internal heat loads.
LOCATION OF APPARATUS
Availability of space for apparatus and duct work is of primary im-
portance when selecting the type of system for a given design. In general,
for large installations, the refrigeration equipment, because of its size,
158
CHAPTER 9 — CENTRAL AIR CONDITIONING SYSTEMS
weight, and operating characteristics, is located in the basement along
with the boilers, fire pumps, and other equipment. The air conditioning
apparatus is generally located where clean outdoor air is readily available,
the designer bearing in mind that supply and return air ducts, steam con-
nections, water and drain connections, and electrical connections must be
made to the equipment proper.
TEMPERATURE OF AIR LEAVING OUTLETS
In comfort conditioning applications, air has been distributed from
properly designed outlets without producing drafts at temperatures
varying from approximately five to thirty degrees below the required
room temperature. Factors influencing the design and selection of air
outlets are: ceiling height, type of ceiling, length of blow, and temperature
and quantity of air to be distributed. Most summer conditioning instal-
lations are designed to supply the air to the conditioned space at from
8 to 15 deg below room temperature. Recently the use of specially
designed nozzles has indicated the possibility of reducing the air quantity
necessary to dissipate a given heat load by introducing the air into the
room as much as thirty degrees below room temperature. Comfort con-
ditioning systems employing differentials greater than fifteen degrees
require special consideration and design experience because high pressure
outlets or nozzles are usually used. Further, care mustte taken to allow
a sufficient air quantity under all load conditions to insure good distri-r
bution. If winter heating, as well as summer conditioning, is to be accom-
plished by the same distributing system, the design of the outlets will be
influenced as discussed in Chapter 22. Industrial systems in which drafts
are not objectionable usually employ a temperature differential equal to
the dew-point depression.
AIR QUANTITY REQUIRED
For calculating the quantity of air required to absorb a given heat gain,
the following approximate formulae may be used :
M = *
60 X 0.24 X (t - t
or, assuming a constant value of 0.075 Ib for d,
_ g. X 55.2
~ 60 X (t - ty)
where
Q = volume of air required, cubic feet per minute.
Hs = total sensible heat gain, Btu per hour.
/ = room temperature, degrees Fahrenheit.
ty = outlet temperature, degrees Fahrenheit.
M = weight of air required, pounds per minute.
d — density of air at the temperature and relative humidity of the, room, pounds per
cubic foot.
Example 1. The total sensible heat gain in a restaurant when held at 80 F is 190,736
Btu per hour. Assuming a 12 deg Fahr temperature differential between the entering
air and the roorn temperatures, which is the same as assuming the dry-bulb temperature
of the entering air to be 68 F, calculate the required air capacity of the system.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Solution.
199,736 X 55.2
60 X 12
minute
If a system similar to the one shown in Fig. 1 is used, 1146 Ib per minute will be the
capacity of the dehumidifier as well as of the fan equipment.
Example 2. If in addition to the 199,736 Btu per hour sensible heat load, the con-
ditioned space has a moisture gain of 384,000 grains per hour, calculate the apparatus
dew point required to give maintained conditions of SO F dry-bulb and 65 F wet -bulb,
with a corresponding 56 % F dew point.
Solution. With 384,000 grains of moisture per hour to be picked up, the entering dew-
point temperature should be low enough so that the addition of this moisture will not
increase the dew point above 56 J^ F.
Grains per pound of air saturated at 56 H F
(Table 5, Chapter 1) 6R.1
384,000
Less: Grains per pound to be picked up, 1146 X 60* '^
Grains per pound allowable in entering air 02.5
This corresponds to an apparatus dew-point temperature of 54.17 F.
Example 8. Illustration of the by-pass system. (See Fig. 2.J
Assume the same data as for Example 2. Instead of passing all of the air through the
dehumidifier for cooling and dehumidifying, a portion may be passed through ^ and the
balance be mixed with the conditioned air at the leaving end of the dehumidifier, the
mixture being proportioned so that the resultant conditions will be those required to
give proper conditions in the area considered.
Solution. The quantity of air to be dehumidified, the quantity to be by-passed, and
the apparatus dew-point temperature may be calculated as follows:
Let
X — percentage of air to be by-passed.
Y = percentage of air to be passed through the dehumidifier.
/3 — apparatus dew-point temperature, degrees Fahrenheit.
The quantity X of 80-F air must mix with the quantity Y of dehumidified air to
produce air with a resultant 65 F wet-bulb temperature. Also, X quantity of air at
56 M F dew point must be mixed with K quantity of dehumidified air to give a resultant
apparatus dew-point temperature of 54.17 F. It is assumed that the air passing through
the dehumidifier is saturated.
Solving simultaneous equations,
80.0Z -f Ytd = 68.00 (3)
56.5JT + Ytd = 54.17 ^
23.5J*T + 0 = 13.83
x = 13-803 * 10° = 59 per cent, air by-passed.
Y - 100 — X =41 per cent, air passed through washer.
The second step is to determine the apparatus dew-point temperature. Substitute X
in either Equation 3 or Equation 4, and solve for id :
80 X 0.59 + /d X 0,41 = 68
gg _ AJ
/d = • - — = 51.2 F, the apparatus dew point.
0.41
160
CHAPTER 9 — CENTRAL Am CONDITIONING SYSTEMS
HEAT TO BE REMOVED BY COOLING AND DEHUMIDIFYING
APPARATUS
Example 4- Assume the same data as for Example 3. If the amount of outside air, at
95 F dry-bulb and 75 F wet-bulb, required for ventilation has been found to be 169 Ib
per minute, determine the refrigeration capacity required.
Solution. As the total weight of the air introduced per minute is 1146 Ib, and 41 per
cent of it goes through the dehumidifier, the total work to be done may be computed
as follows:
Air passing through humidifier, 1146 X 0.41 470 Ib
Less: Outside air for ventilation 169 Ib
Return air 301 Ib
The refrigeration required for the return air is:
Total heat per pound at 65 F 29.65 Btu
Less: Total heat per pound at 51.2 F 20.85 Btu
Requirement for cooling 1 Ib of return air 8.80 Btu
301 Ib X 8.80 Btu = 2649 Btu per minute required to coo! the
return air.
The refrigeration required for the outside air is:
Total heat per pound of outside air 37.81 Btu
Less: Total heat per pound at 51.2 F 20.85 Btu
Requirement to cool 1 Ib of outside air 16.96 Btu
169 Ib X 16.96 Btu = 2866 Btu per minute required to cool the
outside air.
Thus, the total refrigeration required is:
2649 Btu -f- 2866 Btu = 5515 Btu per minute, which is equivalent
to a load of 27.6 tons of refrigeration.
SIZE OF REHEATERS
A properly designed air-conditioning system will have reheaters of
sufficient capacity to heat the conditioned air from the apparatus dew-
point temperature to the outlet delivery temperature. If winter heating
is to be accomplished, consult Chapter 22.
The following general formula may be used to determine the amount of
heat necessary to reheat a given quantity of air:
H\ = 0.24 (ty - /d) M (5)
where
H\ = heat to be supplied to reheater coil, Btu per hour.
Example 5. Assume the same data as for Example 1, and find the amount of reheating
required.
Solution.
H\ = 0.24 (68 - 54.17) 1146 X 60 = 228,200 Btu per hour.
SURFACE COOLING PROBLEM
The amount of coil surface required for a given amount of work is
dependent upon factors previously listed. Obviously, the various types of
surfaces made available by different manufacturers will have different
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
transmission values. It is recommended that the designer consult the
latest manufacturers' catalogs because more accurate ratings are being
issued from time to time.
Airo
60 Fdr
ut
/-bulb
C
3
C
Air m
95 F dry-bulb
78 F wet- bulb
Water in
~~ 50 F
_^ Water out
'50 F + 30F = 80 F
FIG. 4. COUNTER-FLOW SURFACE COOLING DIAGRAM
Example 6. It is desired to cool and dehumidify 30,000 cfm of air at 95 F dry-bulb,
78 F wet-bulb, and 72 F dew point, to a 60 F dew point. Cooling water is available at
50 F in a quantity which will allow a 30 F rise in temperature to be used. The counter-
flow surface cooling used is sketched in Fig. 4.
Solution. The pounds of partially saturated air cooled and dehumidified per hour
equal 60 times the cubic feet of air at 95 F dry-bulb and 78 F wet-bulb brought past the
coil surface per minute, multiplied by the pounds per cubic foot of the air as determined
from Table 3, Chapter 1.
30,000 X 60 X 0.0708 = 127,440 Ib per hour. .
The total heat Ht to be removed per hour by the surface coil is found to be equal to
the pounds of partially saturated air passed over the coil per hour times the difference
between the total heat of air at 78 F wet-bulb and at 60 F wet-bulb.
Ht = 127,440 (40.64 - 26.18) = 1,842,000 Btu per hour.
The latent heat H\ to be removed per hour will be found by multiplying the pounds of
partially saturated air passed over the coils per hour by the difference in the latent heat
of the air per pound at the initial and final dew points.
Hi = 127,440 (17.79 - 11.69) = 777,000 Btu per hour.
The, sensible heat Hg to be removed per hour is equal to the total heat of the air less
its latent heat.
Hs = Ht - Hi « 1,842,000 - 777,000 = 1,065,000 Btu per hour.
Manufacturers' standard ratings for surface coolers are usually based
on the cubic feet of air passed through their equipment per minute,
reduced to the conditions of saturated air measured at a temperature of
70 F. In the present example, to convert the 127,440 Ib of air cooled per
hour to a basis which will permit the use of such standard ratings, it is
necessary to multiply the pounds of air cooled per hour by the specific
volume of the air, and to divide by 60.
127>44° * 13'69 - 29,100 cfm of 70 F saturated air.
ou
The amount of cooling water necessary when a 30 degree rise in its
temperature is to be used is:
'. 1,842,000
30. X 8.34 X 60
162
= 123 gpm.
CHAPTER 9 — CENTRAL AIR CONDITIONING SYSTEMS
With counter flow of air and water, it is necessary to determine the
mean temperature difference between the air and the water in order to
properly use the transmission coefficients given in apparatus rating tables.
J}^ _ £>2
Mean temperature difference = - ^— (6)
Ioge B;
where
Dl = the difference between the temperatures of inlet air and outlet water, degrees
Fahrenheit.
Do = the difference between the temperatures of outlet air and inlet water, degrees
Fahrenheit.
(95 - 80) - (60 - 50) _
— ; — (95 - so) -- 12-33 R
loge (60 - 50)
If from apparatus rating tables based on air velocities over the coils and
water velocities through the coils, it has been found that the transmission
coefficient is equal to 8.0 Btu per square foot per degree difference in
mean temperature between the air and the water, the area of cooling coil
surface necessary will be equal to the sensible heat divided by the trans-
mission coefficient and also by the mean temperature difference.
•« f\fiK AA/"l
' ^ VWoo = 10,800 square feet of cooling coil surface necessary.
o.U
The latent heat is taken out at the same time the sensible heat is
extracted, but no extra surface is required unless the latent heat exceeds
approximately 40 per cent of the total heat. This is because the wetted
surface has a much higher coefficient of transmission. Approximately
10 per cent more surface should be added if the latent heat exceeds 40 per
cent of the total heat.
AUXILIARY EQUIPMENT
Consult Chapters 14, 17, 19, 20, and 22 for information on the air
distribution system; air outlets and inlets; static pressure on fan; fan
motor, and drive; and the control system.
PROBLEMS IN PRACTICE
1 • In summer air conditioning what factors control the difference between
the dry-bulb temperature of the conditioned space and the dry-bulb tem-
perature of the entering air?
1. The duct and supply grille arrangement permitted by architectural and structural
requirements for the particular space, e.g., ceiling height and obstructions on ceilings,
such as beams.
2. The state of activity of the occupants.
3. The outlet velocity at the grille, as limited by noise level requirements.
4. The direction of the jet relative to the occupants.
5. In some cases, the temperature of the available water supply, which may have some
bearing on the air delivery temperature.
2 • What factors determine the volume of conditioned air which must be
delivered to the space?
The sensible heat to be removed, and the allowable temperature differential.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
3 • What factors determine the dew point of the air entering the space?
The maximum dew point desired in the conditioned space, and the moisture gain in the
space per unit weight of air supplied.
4 • Why must the air leaving a dehumidifying type air washer be reheated
before delivery?
The air leaves the dehumidifying air washer saturated at a relatively low temperature
which in most cases is lower than the allowable delivery _dry-bulb temperature. Also,
the air may possibly be carrying a small amount of entrained water which might settle
out in the ducts near the washer and cause corrosion difficulties.
5 • What methods are used for reheating air?
1. Passing it over reheating coils.
2. Mixing it with by-passed air at a higher temperature.
6 • What determines the final temperature of the spray water in a dehumidifier?
Because of the effectiveness of the heat transfer between air and finely divided spray
water in a well designed dehumidifier, the air will be cooled to within 1 or 2 F of the final
water temperature, provided the air velocity through the washer does not exceed 600 fpm.
This final temperature should then be taken as 1 or 2 F lower than the required dew
point of the air leaving the washer.
7 • WThat are the advantages of using counter flow of ah* and water in surface
coolers?
Counter flow results in a higher mean temperature difference than does parallel flow for
the same range of air and water temperatures, which means that less cooling surface is
required. Counter flow permits higher initial water temperatures and also allows a
greater temperature rise for the water. These factors combine to reduce the cost of
circulating and refrigerating the cooling water.
8 • What factors other than cost should be considered in determining whether
to use a central system or another type?
a. Appearance: The equipment must be designed to harmonize with the architecture
of the building.
b. Distribution: The system must maintain adequate and uniform air motion over the
entire conditioned space.
c. Control: The control system must be designed to give effective partial load operation.
9 • Can the central cooling and dehumidifying system be used as an all-year-
round conditioner?
By modifying the control system and adding blast coils or a water heater to the spray
type system, the cooling system will function as one for heating and humidifying. The
surface cooling type may be transformed by modifying the control, and adding another
set of coils and a humidifier.
10 • Will the tons of refrigeration-effect per day be the value calculated in
Example 4 of this chapter times the hours of operation?
No. The tons of refrigeration-effect are functions of the load. The components of the
load vary, that is, the number of people occupying the space, the outdoor conditions, and
the solar radiation will change from hour to hour and from day to day. The calculated
load represents the maximum required for design peak conditions.
11 • Will the quantity of return air required in Example 4 of this chapter be
used all season?
No. When the outdoor wet-bulb temperature becomes lower than the maintained wet-
bulb temperature, it is more economical to use all outside air than to dehumidify the
return air.
164
B
Chapter 10
COOLING METHODS
Methods of Cooling Air, Evaporative Cooling., Dehumidification.,
Silica Gel System, Alumina System, Design of System, Operating
Methods, Steam Jet System, Compressors, Refrigerants, Methods
of Cooling, Condensers
Y using any of the following four methods, or any combination of
them, effective temperature (see Chapter 2) may be reduced.
a. Sensible cooling: Lowering of the dry-bulb temperature by the removal of sensible
heat without change of the dew-point temperature.
b. Dehumidifying: Lowering of the dew-point temperature by the removal of mois-
ture without change of the dry-bulb temperature.
c. Evaporative cooling: Lowering of the dry-bulb temperature through the evapor-
ation of moisture without the addition or the subtraction of heat.
d. Air motion: Increasing the air motion over the body with the resulting higher
evaporation from the skin.
As an example, let the condition be considered of 92 F dry-bulb, with a
40 per cent relative humidity, corresponding to a wet-bulb temperature of
72.8 F, and an effective temperature for still air of 81.1 F. This effective
temperature may be reduced 3.1 F by any of the four basic methods
mentioned, as follows :
First, by lowering the dry-bulb temperature to 85.5 F without changing the dew-point
of 64.2 ; this gives an effective temperature of 78 F.
Second, by reducing the moisture content of the air to 46 grains per pound of dry air
without changing the dry-bulb temperature; this gives an effective temperature of 78 F.
Third, by reducing the dry-bulb temperature to 83.8 F without changing the total
heat of the air. This requires the evaporation of 14 grains of moisture per pound of dry
air, and the effective temperature will become 78 F.
Fourth, by increasing the air movement from still air to 460 fpm, a velocity which will
reduce the effective temperature 3.1 F from 81.1 F to 78 F.
Method to Employ
The best method of reducing the effective temperature in any specific
case will depend on the accompanying circumstances and can be deter-
mined only by a thorough analysis made by a competent engineer.
Generally speaking, the removal from the air of the sensible heat, or
moisture, or both, by sensible cooling or dehumidifying is the most
satisfactory method. Adequate results by the utilization of air motion or
by evaporative cooling are difficult to obtain because of the dependence
of both methods upon climatic conditions beyond the engineers' control
although these methods are much less expensive than the first two
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
mentioned. Cooling by evaporation is satisfactory only when the air to
be cooled is very dry ; air motion as a means of producing cooling effect is
never entirely adequate in the range of high temperatures. Of the two,
evaporative cooling, or adiabatic saturation of the air, is a much more
dependable method which will make more reduction in the effective
temperature than will an increasing air motion within permissible limits.
As an example of this, consider an outdoor condition of 96 F dry-bulb
and 80 F wet-bulb. The effective temperature is 85.7 F and, if the still
air is moved with a velocity of 300 fpm, the effective temperature will be
reduced only 2.0 F while saturation at the wet-bulb temperature would
reduce the effective temperature 5.7 F. At 300 fpm velocity this satu-
rated air would reduce the effective temperature to 75.6 F, thus making a
total improvement of 10.1 F.
Evaporative Cooling
Evaporative cooling is accomplished by passing air through a water
spray in which the water is being continually recirculated. The air,
entering in an unsaturated condition, evaporates a part of the water at the
expense of the sensible heat As this is an adiabatic transfer, the total
heat content of the air remains constant, while the dew point rises and the
dry-bulb falls until the air is saturated. A system1 of ducts and a propel-
ling fan are used to distribute the air in a proper manner.
It will be seen that the- reduction in dry-bulb temperature is a direct
function of the wet-bulb depression of the air entering the ddhumidifier
and that the resulting air temperature is governed entirely by the entering
wet-bulb temperature of the outside air.
Dehumidification
Dehumidification may be accomplished in three ways:
1. By cooling the air below the dew point and causing a part of the moisture contained
to precipitate.
2. By extracting all or part of the moisture by absorption.
3. By extracting all or part of the moisture by adsorption.
As used in this discussion, the term adsorption pertains to the action of
a substance in condensing a gas or vapor and holding the condensate on
its surface without any change in the chemical or physical structure of the
substance and with the release of sensible heat. The term, absorption,
implies a change in the chemical or physical structure of a substance in the
process of dehydrating air. Adsorbers include silica gel and lamisilite;
absorbers include sulphuric acid.
Dehumidification by Refrigeration
Air conditioning imposes requirements on refrigeration equipment not
usually found in general cooling work, so that specially designed apparatus
is often needed to replace that normally used for industrial cooling.
Standard equipment can be adapted to meet air conditioning^ require-
ments but extreme care must be taken to determine the limits of its
applicability.
!See Air Washer Performance in Chapter 11; also Theory of Atmospheric Cooling in same chapter.
166
CHAPTER 10 — COOLING METHODS
In Industrial or process cooling systems the load is fairly constant, noise
in operation is not of paramount importance, space is available or ^re-
latively cheap, condenser water is not a source of worry, and the cooling
system is to a great extent separate and independent of other mechanical
equipment. By contrast, air conditioning, especially as used for space
cooling and comfort work in office buildings, theaters, and places where
people gather requires special consideration of all these factors. Space in
public buildings is limited and condenser water is expensive. Noise
interferes with the occupants, and the cooling equipment must dovetail
with the other air-handling apparatus. Most important, the load fluctu-
ates tremendously and is seasonal.
Heat of Compression
Added to Gas
Low Pressure Saturated
X
Hot In .
Gas
Compressor
High-F
Vessure
Condei
Superheated Gas
*"• Cold in
Evaporator or Cooler
Heat Added to
Refrigerant by
Substance Cooled
1=
Refrigerant by
Cold Out £, . .. .
£\ExpansK)n Valve
for Reducing Pressure .
Hot Out
High Pressure Saturated Liquid
FIG. 1. TYPICAL REFRIGERATION DIAGRAM
A complete discussion of the thermodynamic problems of refrigeration
is given In the Refrigerating Data Book2, 1934, so only a brief description
of the cycle will be given here before the problems peculiar to air con-
ditioning are considered.
The refrigeration system consists of three main parts, the evaporator,
the condenser, and the compressor. Fig. 1 shows a diagram of the cycle.
Heat is absorbed in the evaporator and released in the condenser. The
compressor changes the level of the heat by taking it from a lower to a
higher plane. There are also many valves, accessories, and special devices
necessary for proper operation, which vary somewhat with different types
of cooling systems and different refrigerants.
In. a simple illustrative cycle of a refrigeration system, the liquid
refrigerant under high pressure has both its pressure and temperature
reduced by being expanded through a suitable valve into an evaporator or
cooler. Within the evaporator the low temperature of the refrigerant
allows it to absorb heat from the substance to be cooled, which surrounds
the eyaporator. This absorption of heat increases the pressure of the
*PttbSsfced by American Society of Refrigerating Engineers.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
refrigerant, and a compressor is employed to withdraw enough low-
pressure saturated gas to keep the cooling action of the evaporator con-
tinuous. The withdrawn gas is discharged from the compressor to the
condenser in the form of a high-pressure superheated gas which includes
the heat added through its compression. In the condenser, because heat
is taken from the gaseous refrigerant by the condensing medium, usually
water, the refrigerant again becomes the high-pressure saturated liquid
with which the cycle started.
The cooling water, which may come from a deep well or from a city
main, may be utilized for some purpose after it has been warmed a few
degrees in the condenser, or after use it may be exposed to the atmosphere
J3RY AIR
<
COOLER
ADSORPTION
FAN
ACTIVATION
FAN
WET
GAS HEATER
FIG. 2. SILICA GEL AIR-CONDITIONING SYSTEM — SINGLE STAGE ADSORPTION
in a spray pond or cooling tower and have its temperature reduced to a
point where the water may be used again. (See Chapter 11.)
Silica Gel System
Silica gel is a chemical composition made from sodium silicate and acid,
the chemical formula being SiO2. It has an appearance greatly resembling
that of clear quartz sand but it differs in structure in that the crystals
are highly porous, with voids constituting 41 per cent by volume although
the pores are microscopic in size. This material possesses the property of
being able to adsorb a substantial portion (about 25 per cent of its own
weight) of moisture from the air without any increase in its volume.
After the silica gel has become " saturated " or has adsorbed moisture to
the limit of its capacity, the moisture may be driven from it by the
application of heat, again without change in the structure, volume, or
chemical composition of the silica gel. This cycle may be repeated in-
definitely. When applied to air conditioning the silica gel which is
exposed to the air reduces the moisture content in the air and releases
sensible heat which may be readily removed from the air. A typical
diagram is shown in Fig. 2.
168
CHAPTER 10 — COOLING METHODS
Practical Application of Silica Gel
Silica gel has two applications when used to replace refrigeration. In
the one principally used, the air from which moisture is to be extracted is
taken through silica gel beds by suction or pressure fans, and by means of
this process the moisture becomes adsorbed by the silica gel and the air
leaves at a lower dew point and a higher sensible temperature than those
at which it entered. If this air is passed over surface coolers in which tap
water or another cooling medium is flowing through tubes, a certain
amount of sensible heat will be removed. The air leaves the surface cooler
or interchanger with the same dew point with which it emerged from the
silica gel beds, but with a lower dry-bulb temperature, although the dry-
bulb temperature may be higher than the temperature of the air entering
the silica gel beds.
In another method, the first two of the steps outlined are duplicated,
and in addition the air is carried through a spray type washer. Because
the air enters the washer with a low wet-bulb, and because adiabatic
saturation will take place at a temperature close to the entering wet-bulb,
considerable cooling of the air can be accomplished; but this can be done
only with a consequent increase of the dew point.
It is necessary to reactivate the silica gel after it has adsorbed about
25 per cent of its own weight in the form of moisture. As reactivation
requires a high temperature and since silica gel is only active at low tem-
peratures, cooling of the beds must also be completed before they can be
used again. This necessitates three stages in the silica gel containers and
requires either three beds of silica gel or one bed divided and automatically
put in position. The reactivation is usually done by means of gas or oil
fires and the cooling of the beds by means of indirect water cooling or by
means of small quantities of dehydrated air taken from the system beyond
the interchanger.
Alumina System of Adsorption
Activated alumina contains a trifle over 91 per cent of aluminum 'oxide,
AlzOz, which material will adsorb nearly 100 per cent of the vapor in the
air up to about 8 or 10 per cent of the weight of the adsorbing material,
after which the adsorption falls off gradually as the saturation point is
approached. The application is quite similar to that employed for silica
gel; that is, the material is exposed to the air flow and after reaching
about 75 per cent saturation is reactivated by removing the moisture
adsorbed by means of applied heat. The actual scheme generally fol-
lowed in the use of this material for continuous service varies somewhat
from silica gel inasmuch as the material is placed in three units which are
used consecutively for the different steps. These steps permit each unit
to operate as follows :
a. In series with the preceding unit.
b. Alone.
c. In series with the following unit.
This plan allows for adsorption, reactivation, and cooling, in a manner
similar to that used with silica gel.
Taking a single unit, when it is in the a step and operating with the
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preceding unit, the alumina adsorbs approximately 25 per cent of the
moisture in the air and takes up about 1.3 per cent of its weight of water.
During the second step when it is operating alone, it takes up 100 per cent
of the moisture in the air until the weight of the water adsorbed is brought
up to about 6.7 per cent. During the third step when the unit is operating
with the succeeding unit, it extracts about 75 per cent of the moisture in
the air until the water weight adsorbed comes up to about 10 per cent of
the weight of the adsorber. The time allowable for reactivating is equal
to the time occupied by the second unit adsorbing alone, plus the time
when the second and third units are adsorbing in series, plus the time
when the third unit is adsorbing alone, at the expiration of which time the
first unit will be again required.
The temperature of air used for alumina reactivation is usually between
300 and 700 F and the air flow rate will have to be higher with the low
temperature air than it will be with reactivating air of higher temperature.
For example, air at 400 F for reactivating will, at 10 cu ft per hour per
pound of alumina, require about 6 hours for reactivation. In the three
unit system, after reactivation the cooling of the activated alumina may
be carried out with considerable rapidity by using dry air from the adsorp-
tion unit for circulation through the unit which has just completed reacti-
vation. The final temperature of the unit before it goes back into service
should be not over 200 F. As a basis for computing the amount of cooling
air required for reactivation, each cubic foot of cooling air has been found
capable of removing 2.2 Btu when heated from 85 to 200 F and of provid-
ing a sufficient margin of safety in operation.
Design of System
When designing air conditioning systems, the capacity of equipment is
decided by selecting apparatus of sufficient size to maintain predetermined
temperatures and humidities in treated spaces when arbitrarily estab-
lished maximum atmospheric temperatures occur coincident with given
conditions of population, lighting, and power consumption. These factors
determine the maximum duty of the cooling system. The duty does not
necessarily determine the size or capacity of the refrigeration apparatus.
The refrigerating capacity is expressed in tons, each ton being equal to the
absorption of the heat given up by one ton of ice at 32 F melting to water
at 32 F in 24 hours. This is equivalent to heat absorption at a rate of
approximately 200 Btu per minute, or 12,000 Btu per hour.
After the maximum duty is determined, the other factors concerning
the installation must be investigated. The total heat to be removed by
the cooling system has many sources, some substantially constant and
others extremely variable. These sources can be roughly classified as
follows, the first column indicating the order in amount and the second
the order in variability:
1. Fresh air supplied. 1. Fresh air supplied.
2. Population. 2. Transmission through the structure.
3. Transmission through the structure. 3. Light and power consumed.
4. Light and power consumed. 4. Population.
By combining these two columns, a third grouping is obtained - as
follows:
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CHAPTER 10 — COOLING METHODS
1. Fresh air supplied. 3. Population.
2. Transmission through the structure. 4. Light and power consumed.
In this last arrangement, the first two items are governed by atmos-
pheric conditions and they are therefore subject to tremendous fluctu-
ations in value. As they generally form 40 to 60 per cent of the entire
maximum load, the duty of the cooling system will be much less than
maximum most of the time.
The transmission through the structure is especially influenced by the
sun. (See Chapter 8.) In many cases, because of the heat flow resistance
of the structure, the heat from the sun is retarded until it is compensated
for by a reduced general temperature out-of-doors.
A survey of Weather Bureau records indicates that maximum tempera-
tures occur less than 5 per cent of the cooling period and also that the
duration of peak conditions is never more than three or four hours.
Two factors control the size of the refrigeration system, the evaporator
or suction temperature, and the condenser or head temperature. With
the knowledge that the system will operate most of the time with a load of
not over 60 per cent of maximum, and that maximum demands will occur
infrequently and only for short periods, some provision must be made to
insure economical operation under average conditions. This can be done
by overloading the machine under extreme demands and basing the design
on normal or average loads. Flexibility in arrangement can be provided
in several ways.
Variations in load change the efficiency of any machine and a refrigera-
ting system can be costly and inefficient if improperly designed or operated.
Fortunately, the trouble can be concentrated in the compressor and the
problem relieved of many complications. It is comparatively easy to
furnish condensers and evaporators to carry the maximum load so
arranged that they will function properly at small demands. They affect
the compressor performance to some extent but most of the compressor
problems are in the machine itself.
Variations in load are usually effected by lowering the suction tem-
perature and pumping a larger volume of gas per ton through a greater
pressure range. This is possible because the latent heat of the refrigerant
remains nearly constant throughout the small range used and the specific
volume varies rapidly with change in pressure. As the compressor must
remove the refrigerant evaporated, the evaporator temperature fixes the
displacement required. The objection to such method is that the total
power consumed remains nearly constant and the power per unit of
cooling increases rapidly as the total output is reduced. Such operation
is satisfactory as long as the load is kept within 10 per cent of the rating
of the compressor but this condition does not commonly occur in air
conditioning applications.
Operating Methods
It is possible to divide the entire refrigeration system into a number of
small units, which will allow cutting in and out of compressors and con-
densers as the load fluctuates. This, however, is an expensive method as
a number of small units are usually more expensive than one large unit.
There is a certain amount of duplication of equipment necessary, which
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tends to increase the initial cost of the system and which makes the fixed
charges, applicable to the operation of the air conditioning and cooling
system, greater than necessary.
A second method of providing for economy of operation is to have
storage capacity which can be utilized during the peak period. A further
reference to the Weather Bureau records indicates that maximum con-
ditions prevail during the day for not more than three hours, and con-
sequently the refrigerating system can be run for a longer period at
maximum efficiency with tanks to store cold water or brine for supple-
menting the actual output of the refrigerating equipment when the load is
more than the machine will carry. This situation brings complications.
Storage tanks require space and extra apparatus, which increase the cost
of the entire system, and further, it is difficult to determine what the size
of the compressor should be because of the other variables which enter the
problem. Depending upon the availability of storage space, the com-
pressor could be designed for any reasonable percentage of the maximum
load, so the smaller the compressor, the larger the storage space, and
vice versa.
A third method is to provide in the compressor itself some means of
reducing the capacity. This can be done by varying the speed and con-
sequently the displacement of the compressor, or by varying the dis-
placement, either by a partial by-pass of the cylinder or by a clearance
pocket in the head of the cylinder when reciprocating compressors are
used. It might be assumed that the efficiency would remain practically
constant. This is not correct, inasmuch as the machine friction remains
constant with the by-pass or clearance pocket method and this raises the
power required per ton of refrigeration developed. Also, the volumetric
efficiency of the machine falls off rather rapidly when the clearance pocket
or partial by-pass is used. By varying the speed of the compressor, the
efficiency of the power unit falls off as the speed is reduced, while the
compressor friction remains constant. Of the two methods, the clearance
pocket or partial by-pass of the cylinder is probably the more efficient
for general use.
Another method of operation is the automatic starting and stopping of
the refrigerating machine, with the automatic control designed to function
as the load varies. This, however, is not considered good practice as
mechanical troubles develop and the life of the system is impaired. If
the equipment is kept in good condition, however, the machine will
operate at maximum efficiency so long as it runs. The frequent starting
and stopping of large compressors is liable to cause the power factor to
decrease if adequate allowance is not made.
All of the methods described are used from time to time.
The methods of varying the output of a refrigeration system which have
been outlined apply to the reciprocating type of compressor, although
variations in the speed of the compressor to change the refrigerating
output are common to all types of mechanical refrigeration.
There is a further method of controlling the compressor output which is
particularly adaptable to the centrifugal type of machine. This is accom-
plished by varying the amount of condensing water used with the fluctu-
ation in demand load. Because of the characteristics of the centrifugal
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CHAPTER 10 — COOLING METHODS
type of apparatus, as the condensing water quantity is reduced and the
condensing temperature consequently raised, the discharge pressure of
the centrifugal machine rises correspondingly and the horsepower input
to the machine falls off. While this reduces the total power input to the
machine, it does not necessarily reduce the power input per ton of re-
frigeration developed, as the power input does not drop with a rising dis-
charge pressure as fast as the refrigerating effect produced drops. It is a
method, however, which shows marked economies over the method
generally used by the operating engineer, which is to lower the suction
pressure in order to reduce the refrigerating output of the system.
Steam Jet System
So far the discussion has been confined to reciprocating, centrifugal, and
rotary compressors. The steam jet type of compressor, under certain
circumstances, is desirable for use in air conditioning. Fig. 3 shows a
complete flow diagram of the system. The power used for compressing
"^a EVAPORATOR
CHILLED VUTER DISCHARGE
FIG. 3, DIAGRAM OF STEAM JET REFRIGERATION UNIT
the refrigerant is steam, taken directly from the boiler, thus eliminating
the mechanical losses of manufacturing electric current. As the compres-
sion ratio between the evaporator and condenser under normal circum-
stances is large, the mechanical efficiencies of the equipment are somewhat
lower than those of the positive mechanical type of compressor ; also the
condensing water requirements are considerably greater, as both the
refrigerant and the impelling steam must be condensed.
The steam jet system functions on the principle that water under high
vacuum will vaporize at low temperatures, and steam ejectors of the type
commonly used in power plants for various processes will produce the
necessary low absolute pressure to cause evaporation of the water.
Fig. 3 shows a typical water cooling application. The water to be
cooled enters the evaporator and is cooled to a temperature corresponding
to the vacuum maintained. Because of the high vacuum, a small amount
of the water introduced in the evaporator is flashed into steam, and as
this requires heat and the only source of heat is the rest of the water in
the evaporator tank, this other water is almost instantly cooled to a
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temperature corresponding to the boiling point, determined by the
vacuum maintained. The amount of water flashed into steam is a small
percentage of the total water circulated through the evaporator, amount-
ing to approximately 11 Ib per hour per ton of refrigeration developed.
The remainder of the water at the desired low temperature is pumped out
of the evaporator and used at the point where it is required.
The ejector compresses the vapor which has been flashed into the
evaporator, plus any entrained air taken out of the water circulated, to a
somewhat higher absolute pressure, and the vapor and air mix with the
impelling steam on the discharge side of the jet. The total mixture of
entrained air, evaporated water, and impelling steam is discharged into a
surface condenser at a pressure which permits the available condensing
medium to condense it. The resulting condensate is removed from the
condenser by a small pump, from which it can be discharged to the sewer
or returned to the system in the form of make-up water, or part of it may
be returned to the boiler feed pump.
As the normal temperature of water required for air conditioning
purposes is between 40 F and 50 F, with an average temperature of
approximately 45 F, this type of water cooling is particularly desirable,
as the efficiencies and operating costs compare very favorably with other
types of refrigerating equipment, especially in view of the fact that the
cooling apparatus is, as a general rule, less expensive to install.
Approximately three times as much condenser water is required for the
steam jet cooling system as would be necessary with other types of
mechanical refrigeration, but as the system can be designed with a large
number of jets, each of which can be cut off as the load falls below maxi-
mum, constant refrigerating efficiency is maintained and frictional losses
and volumetric inefficiencies are kept at a minimum.
The slight amount of air which may be entrained in the cooled water is
removed by a small secondary ejector which raises the pressure sufficiently
so that the air can be discharged to the atmosphere. A small secondary
condenser, of course, is necessary to condense the steam used in the
secondary jet.
Steam jet refrigeration has an advantage where cooling towers are used
for supplying the condensing liquid, as there is a great saving in the
amount of steam used per ton of refrigeration. As the outdoor weather
conditions vary the load on the cooling system, the compression ratio
between the condenser and evaporator can be reduced and less propelling
steam need be used per ton of refrigeration developed. Roughly, in air
conditioning work, mechanical compressors show a falling off of 30 to 40
per cent in the power input when using the most economical arrangement
of compressors, as the load varies from 100 per cent to 25 per cent of the
rated capacity; whereas with steam jet cooling equipment, the amount of
steam required for producing the necessary refrigerating effect falls off in
direct proportion to the load on the system. When steam refrigeration is em-
ployed with cooling towers, the efficiency increases as the output is reduced.
Compressors and Refrigerants
There are many different types of compressors, a number of refrigerants,
different types of evaporators, condensers and arrangements of the cycle,
type has its particular place and
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The generally used compressors are of the following types:
1. Reciprocating compressors.
2. Centrifugal compressors.
3. Rotary compressors.
4. Steam jet compressors.
Over-all efficiency of the compressor in smaller commercial installations
is not as important a requirement as that the whole unit require little
attention and make a minimum of noise. The noise level when the fan,
sprays, and compressor are in full operation should not exceed 25 decibels.
High compressor efficiency appears as an important factor only in the
larger industrial air conditioning systems.
The refrigerants in most general use in commercial and industrial air
conditioning are here listed in the order of their inoffensive odor charac-
teristics :
1. Water vapor.
2. Carbon dioxide.
3. Dichlorodifluoromethane.
4. Dichloromethane, sometimes called methylene chloride.
5. Methyl chloride.
6. Ammonia.
7. Sulphur dioxide.
The- various types of compressors bear varied relationships to the
refrigerants used in both commercial and industrial air conditioning.
Reciprocating compressors are generally used for any of the refrigerants
listed except water vapor, dichloromethane, or other low pressure refri-
gerant, and they are used in both commercial and domestic air conditioning
systems. They have been developed to a point where their efficiency is
high and their operation very satisfactory. Relatively low speed opera-
tion makes them desirable for general use in large installations. They are
of two types, vertical and horizontal, either single or double acting. The
horizontal double-acting compressor is not generally used in air condition-
ing except when carbon dioxide is used as the refrigerant in the larger
industrial systems. Vertical, single-acting, encased crank, reciprocating
compressors of the uniflow type with valves in the pistons have proven
reliable and are used in capacities from 1 hp to more than 100 hp. Re-
ciprocating compressors can be used with more refrigerants than other
types of compression units. For instance, when carbon dioxide is used as
the refrigerant, a reciprocating compressor is required because of the
extremely high pressures and the relatively high ratio of compression.
The production of refrigeration at temperature levels from 25 F to
55 F for general air conditioning involves special types of refrigerating
compressors. Among these are:
1. Centrifugal compressors using a volatile refrigerant.
2. Centrifugal compressors using water as a refrigerant.
3. Steam jet or vacuum systems using water as a refrigerant.
4. Rotary compressors using a volatile refrigerant,
.first two types, centrifugal compressors, using dichloromethane or
water vapor, can theoretically be used with any of the other refrigerants,
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but the resulting loss in efficiency with the higher pressure gases limits the
centrifugal compressor to the two refrigerants named. At the present
time the centrifugal compressors are limited to air conditioning systems of
about 75 hp and more. Centrifugal compressors are usually built in two
or more stages where the compression ratio is high, and their design
follows closely that of any other centrifugal equipment, such as general
service pumps and fans.
Steam jet compressors which have recently entered the field are simple
and compact and, having no moving parts, they produce practically no
vibration but are not economical for water temperatures much below
40 F or where the cost of generating steam is higher than the cost of
operation with other prime movers.
Rotary compressors are generally used for methyl chloride and dichloro-
difluoromethane because of their relatively low pressure and compression
ratios. These compressors find widest use for fractional tonnage duty.
The source of condensing water to some extent governs the type of
refrigerant used. If condensing water is available at temperatures of not
more than 70 to 75 F any of the refrigerants mentioned can be used
economically, but if the available condensing water temperature is above
80 F, carbon dioxide becomes uneconomical as its critical temperature is
approximately 88 F. A condensing water temperature over 80 F makes
the power required for compression high. All refrigerants have critical
temperatures and pressures sufficiently high so that their efficiency is not
materially affected by the condensing water temperatures, except in so
far as this temperature affects the compression ratio. Steam jet cooling
systems can use water up to 85 F, or even slightly warmer.
The applicability of the various refrigerants is interesting. Carbon
dioxide is limited by the condensing water temperature; the power con-
sumption is slightly higher than that of other refrigerants; and the pres-
sures are three to four times that of ammonia.
The condenser pressures of methyl chloride and dichlorodifluromethane
are approximately one-half that of ammonia.
Ammonia, probably the best known refrigerant, has the disadvantage
of being toxic, and under certain circumstances explosive, corrosive, and
irritating, even in small quantities in the atmosphere. Ammonia is used
exclusively in the larger indirect or brine cooling air conditioning systems.
Sulphur dioxide is corrosive and irritating even in small quantities in
the atmosphere and it is toxic under certain circumstances.
Dichloromethane operates at pressures below that of the atmosphere,
and it is to some extent toxic.
Dichlorodifluromethane under normal circumstances is non-toxic, non-
irritating, and non-explosive, but under high temperatures it breaks
down into several obnoxious, poisonous components.
Methyl chloride, under certain conditions, is explosive and slightly
toxic.
The steam ejector water vapor system has none of the disadvantages of
toxicity, explosiveness and corrosiveness encountered in the other refri-
gerants, but the system operates at less than atmospheric pressure. This,
however, is not an important factor as there are no moving parts in the
compressor and the possibility of inleakage of air is remote as all of the
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CHAPTER 10 — COOLING METHODS
equipment can be welded air and water tight. The supply of water is
inexhaustible, and as a refrigerant, the make-up cost is negligible. The
same boiler equipment can be used for heating in winter and for cooling
in summer.
Electric Motors
The motors used for driving compressors can be roughly classified in
three groups: synchronous, multispeed, or variable speed. Further infor-
mation on motors may be found in Chapter 17.
Coolers
The types of coolers used in connection with air conditioning work fall
into three general groups. The first is the direct cooling of water; the
second, direct cooling of air; and the third, cooling of brine for circulation
in a closed system, which can cool either water or air. One method of the
direct cooling of water is to install direct expansion coils in the spray
chamber so that the water sprayed into the air comes in direct contact
with the cooling coils. Another common and efficient method of cooling
spray water is to use a Baudelot type of heat absorber where the water
flows over direct expansion coils at a rate sufficiently high to give efficient
heat transfer from water to refrigerant.
Another type of spray water cooler is the shell and tube heat exchanger
in which the refrigerant is expanded into a shell enclosing the tubes
through which the water flows. The velocity of the water in the tubes
affects the rate of heat transfer, and as the refrigerant is in the shell com-
pletely surrounding the tubes at all times, good contact and a high rate of
heat transfer are insured. The disadvantage of such a system is that with
the falling off of load on the compressor the suction temperature or the
temperature in the evaporator drops and there is a possibility of freezing
the water in the tubes, which, of course, might split the tubes and allow
the refrigerant to escape into the water passage. This danger can be
eliminated by automatic safety devices.
Another system of cooling spray water is to submerge coils in the spray
collecting tank, or in a separate tank used for storage. The heat trans-
mission through the walls of the coils, however, is low and a great deal
more surface is required than for any other type of cooler. However, with
large storage tanks this type of cooling can be utilized to advantage.
When direct cooling of air is employed, the refrigerant is inside the coil
and the air passes over it. Cooling depends upon convection and con-
duction for removing the heat from the air. The type of coil used can be
either smooth or finned, the finned coil being more economical in space
requirement than the smooth coil. The fins, however, must be far enough
apart so as not to retain the moisture which condenses out of the air.
The indirect cooler, where brine is cooled by the refrigerant and the
resulting cold brine is used to cool either air or water, introduces several
other considerations. It is not the most economical from a power con-
sumption standpoint, as it is necessary to cool the brine to a temperature
sufficiently low so that there is an appreciable difference between the
average brine temperature and that of the substance being cooled. This
requires that the temperature of the refrigerant must be still lower, and
consequently the amount of power required to produce a given amount of
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refrigeration increases due to the higher compression ratio, but there are
other considerations which make such a system desirable. In the first
place, where a toxic refrigerant is undesirable or cannot be used, due to
fire or other risks especially in densely populated areas, the brine can be
cooled in an isolated room or building and then be circulated through the
air conditioning equipment in perfect safety because it is used to cool the
water or air, without any possibility of direct contact between the air and
refrigerant.
When an indirect system of cooling is used, it will be found that the heat
transfer rate of the water cooler is considerably higher as a general rule
than that of a direct expansion cooler for the same requirements. With
direct expansion interchanges, it is almost impossible to keep the entire
system flooded with liquid, whereas with brine interchangers the cooling
medium completely fills the space of the interchanger and perfect contact
is insured.
Ice may be used for chilling water or air for conditioning work. Its
application is limited because of the cost of ice, although the efficiency of
cooling is higher than any other water cooling system. The word "water
cooling" is used advisedly in that the direct cooling of air by ice is, while
not impossible, rather impractical. It might be said that ice coolers are
economical for systems requiring a maximum of 20 tons per 24 hours
where the load fluctuates considerably, and it is possible to introduce ice
only as it is required to cool water. The most general method of cooling
water with ice is to spray the water over the surface of the ice, insuring as
much contact as possible and approximating the same performance as the
Baudelot type of cooler. Because of the large fluctuations in load in the
air conditioning system, the higher cost of refrigerating effect when ice is
used is offset by the fact that there are no motor and condenser in-
efficiencies under partial load. Also, because the cost of the mechanical
refrigeration equipment for the small system is so much higher per unit of
effect, the fixed charges are small enough to overbalance the extra cost
of the ice.
Condensers
Condensers are usually either the double pipe type or^the shell and tube
type. Shell and tube condensers are almost identical with coolers.
Double pipe condensers are arranged so that water passes through the
inner of two concentric pipes, and refrigeration passes through the
annular space in the outer pipe. Where possible, there should be counter
flow of the refrigerant and the condensing water to maintain maximum
temperature differences.
The amount and temperature of the condensing water determine the
condensing temperature and pressure, and indirectly the power required
for compression. It is, therefore, necessary to strike a balance so that the
quantity of water insures economical compressor operation.
As part of the condenser, or attached to it, there must be storage space
for liquid refrigerant. The installation of all equipment should be made
accessible for inspection, repair, and cleaning. Both the coolers and
condensers should have space for pulling tubes.
Because there is a decided tendency to conserve the water in city mains
and most large cities are restricting the use of water, in order to use air
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conditioning systems and refrigeration equipment it is often necessary to
install cooling towers. The cooling towers, unfortunately, produce the
warmest condensing water at the time when the load on the system is
greatest, so that the refrigeration equipment must be designed to meet
not only the maximum load at normal conditions, but also the maximum
load at abnormal condensing water temperatures. If properly designed,
this makes little difference in the efficiency of operation throughout the
year except at those times when the condensing water temperature is
highest. As this occurs only for 5 per cent of the entire cooling period it
can be disregarded as a factor in establishing yearly operating costs.
The cooling tower has a certain advantage over the use of water from
the city mains in that the temperature of the condensing water varies
directly with the outdoor temperature and, as pointed out, the refrigera-
tion load also varies with this temperature. Certain economies are pos-
sible when a cooling tower is used which cannot be achieved by the use of
condensing water from city mains, even where the city water temperature
is extremely low. Normally, the lowest city water temperature met during
the summer months is from 65 to 70 F. This temperature range takes
place for the entire cooling period, regardless of what the outdoor tempera-
tures are. With the cooling tower, the temperature of the condensing
water may rise to 80 or 85 F under maximum conditions, but under less
than maximum conditions the temperature of the water off the cooling
tower drops considerably, and it has been established that 50 per cent of
the time the outdoor wet-bulb temperature varies from 60 to 70 F and the
cooling tower water, therefore, for the same periods, varies from 65 to 75 F,
When the outdoor wet-bulb temperature drops below 60 F, which occurs
approximately 30 per cent of the time, the condensing water temperature
is still lower. The cost of water used for condensing is negligible, as the
only water required is that used to make up the loss by evaporation in the
cooling tower itself. See also Chapter 11.
PROBLEMS IN PRACTICE
I • In a locality where the electric power rate is based on a demand charge, it
is desired to install the smallest possible compressor motor which will provide
summer cooling for a 300-seat restaurant which operates 6 hours per day from
II a.m. to 2 p.m., and from 5 p.m. to 8 p.m. The refrigeration load at the peak
is 28 tons. If the load factor for both the noon and evening meals is 70 per cent,
discuss the type of equipment which would take the greatest advantage of the
reduced power rate at low kilowatt demand.
A storage system using a chilled water storage tank would permit the installation of a
refrigeration system having the smallest motor.
For a 28-ton system operating 6 hours per day at a 70 per cent load factor, on the maxi-
mum day the total heat removed would be,
28 tons X 6 hr X 0.7 = 117.5 ton-hours per day.
If a compressor were to operate 24 hours at a constant rate, its average capacity would be
24 hours = 4"^ t0ns' °r aPProx*mately 5 tons. If operated 12 hours per day, the
compressor capacity would have to be increased to 10 tons.
A water storage tank would store the refrigeration and allow off-peak operation, so a
smaller compressor motor could be used. However, the suction temperature at which the
compressor would be operated would be lowered approximately 5 to 10 F. This would
increase the horsepower per ton of refrigeration, when dichlorodiflouromethane is used,
approximately 10 per cent for a 5 F reduction and 24 per cent for a 10 F reduction in the
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suction temperature. Rather than store the water at too cold a temperature, it would
be more economical to install a larger storage tank and use a higher temperature.
A 5-ton compressor running during periods when there are no customers, namely, during
the 15 hours from 8 p.m, to 11 a.m. will have stored 15 hr X 5 tons, or 75 ton-hours, of
refrigeration in the storage tank by 11 a.m. As one ton-hour equals 12,000 Btu, 75 X
12,000 Btu, or 900,000 Btu, will have been stored.
If the apparatus dew-point temperature is 54 F, and the chilled water is supplied to the
air washer at 48 F, it will leave at 54 F. If the water in the storage tank is at 40 F, the
temperature difference between the stored water and the water entering the wrasher will
be 48 F - 40 F = 8 F. This is equivalent to an available 8 Btu of cooling effect per Ib
onn ono
of water stored. Therefore, 5 — or 112,500 Ib of water must be stored. This is
112,500
8
= 13,500 gal water to be stored, which equals
13,500
1800 cu ft of water.
The storage tank to hold this water might be 6 ft high, 7 J^ ft wide, and 40 ft long. Should
this volume prove impractical, a proportionately smaller tank could be used if the water
storage temperature were reduced. Should a 10-ton refrigeration system be used, the
water quantities and tank capacity could be reduced by one half, and the refrigeration
plant need not be started until 8 a.m. daily, which might prove of additional advantage.
If refrigeration is stored by freezing ice on coils, considerable storage space will be saved
but more power input per Btu of cooling will be required.
2 • For condensing purposes, an air conditioning system uses city water which
has an average 70 F supply temperature. The following tahle lists the number
of hours per year during which definite wet-bulb temperatures and corre-
sponding refrigeration rates pertain.
Wet-Bulb
Temperature
F
No. of
Hours
per Year
Refrigeration
Required
Tons
80
6
284
79 - 75
100
233
74 - 70
277
183
69 - 65
330
157
64-60
277
144
59 - 55
158
79
54 - 50
52
37
Total 1200 hours
If the power requirements of a dichlorodifluoromethane refrigeration system
are in accordance with the following data on partial load operation, determine
the seasonal power cost at 2 cents per kwhr:
284 233 183 157 144 79 37
Tons of Refrigeration
Kw per ton
Seasonal power cost :
0.89 0.89 0.87 0.86 0.86 0.93 0.97
WET-BULB
TEMPERATURE
P
TON-HOURS
KWHR
80
79 - 75
74 - 70
69 - 65
64 - 60
59 - 55
54 - 50
Totals
6 X 284
100 X 233
277 X 183
330 X 157
277 X 144
158 X 79
52 X 37
« 1,704
= 23,300
= 50,700
= 51,800
= 39,900
= 12,500
= 1,920
1,704 X 0.89
23,300 X 0.89
50,700 X 0.87
51,800 X 0.86
39,900 X 0.86
12,500 X 0.93
1,920 X 0.97
= 1,517
= 20,750
« 44,100
« 44,500
= 34,300
= 11,600
= 1,860
181,824 ton-hours
158,627 kwhr
180
CHAPTER 10 — COOLING METHODS
The 158,627 kwhr at 2 cents per kwhr will cost S3, 173.
158,627 kwhr
The average consumption will be ,Q1 Q0. - r - = 0.8/3 kw per ton.
i.oifOA'z ton-nours
3 • Using the data from Question 2, if city water costs 20 cents per thousand
gallons, and if 1.25 gallons are used per minute per ton, estimate the annual
\vater cost.
60 X 1.25 = 75 gal per ton-hour.
181,824 ton-hours X 75 = 13,620,000 gal per year.
13,620,000X80.20
----- — i7\nn -- ~~ — =
lUuU
^ , r
, the yearly cooling water cost.
4 • Using the data of Question 2, if a cooling tower were installed for re-using
the condensing water, estimate the annual operating cost of a dichlorodifluoro-
m ethane refrigeration system if the final temperatures of the water leaving the
cooling tower and the kilowatt input per ton are the following :
Tons 284 233 183 157 144 79 37
Temperature of water
leaving tower, F 86.7 81.8 76.5 72.1 66.4 61.3 55.6
Kw input per ton 1.10 0.94 0.85 0.80 0.74 0.59 0.62
WET-BULB
TEMPERATURE
F
TON-HOURS
Kw PER TON
1
KttHR
80
1,704
X
1.10
=
1,875
79 - 75
23,300
X
0.94
=
21,900
74 - 70
50,700
X
0.85
=
43,300
69 - 65
51,800
X
0.80
=
41,400
64-60
39,900
X
0.74
=
29,500
59 - 55
12,500
X
0.59
=
7,370
54-50
1,920
X
0.62
=
1,200
Totals
181,824 ton-hours
146,545 kwhr
The 146,545 kwhr at 2 cents per kwhr will cost $2,931.
~ .. .„ . 146,545 kwhr
The average consumption will be 101 00. r =
fe ^ 181,824 ton hours
0.805 kw per ton.
5 • If a steam ejector system were used to secure the refrigeration for the air
conditioning system of Question 2, compute the annual steam cost if steam is
sold for 53 cents per thousand pounds and if there is an average steam con-
sumption of 20 Ib of steam per hour per ton when used with a cooling tower
system.
181,824 tons X 20 Ib of steam per ton = 3,636,480 Ib of steam.
The 3,636,480 Ib at 53 cents per thousand pounds will cost $1,929.
6 • From the data given in the following tahle covering auxiliary equipment,
make a comparison between the operating costs of the complete dichlorodi-
fluorome thane system of Question 4 and the complete steam ejector cooling
system of Question 5. A cooling tower is used for condenser water recovery.
Plant Operation
Dichlorodifluoromethane
System
Steam Ejector
System
Hours of operation.
1200
1200
Cooling tower fan, hhp
17.8
35.6
Cooling tower pump, bhp
30.2
47.8
Chilled water, gpm
1200
1200
Discharge head on chilled water
SyfttftTM^ ft
75
75
Pump efficiency, per cent
75
75
Motor efficiency, per cent
80
80
Chilled water temperature, F
46
46
The flash tank or evaporator of the steam ejector system is of the open type,
the flash water being pumped directly to the sprays of the washer used for
cooling the air.
181
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Dichlorodifluoromethane System:
Power requirements,
Cooling tower fan 17.8 bhp
Cooling tower pump 30.2
Total 48.0 bhp
The water cooler in a dichlorodifluoromethane system of the surface type requires no
additional pumping head other than the friction drop through the cooler, which in this
problem is estimated to be 10 ft. The total pumping head is, therefore, 75 -f 10 = So ft.
Power required for the chilled water system will be,
1200 gpm X 8.34 Ib per gallon X 85 ft head
33,000 ft Ib X 0.75 pump efficiency P'
34.3 bhp X 0.746 X 1200 hr
- n 00 - ; - ^— : - = 08,000 kwnr.
0.80 motor efficiency
Thus, the total power required by the auxiliary equipment will be
53,700 + 38,300 = 92,000 kwhr.
The 92,000 kwhr at 2 cents per kwhr will cost $1,840
The power cost of refrigeration, from Question 4, is 2t931
The total annual power cost, using a dichlorodifluoromethane system, is $4,771
Steam Ejector System:
Power requirements,
Cooling tower fan 35,6 bhp
Cooling tower pump 47.8
Total 83.4 bhp
T> f r . ^ 83.4 bhp X 0.746 X 1200 hr no OAn , ,
Power for cooling tower systems = - — £ - - — *-&-. - = 93,300 kwhr.
0.80 motor efficiency
Iii the flash tank or water cooler of the steam ejector system, the water is at a pressure
corresponding to the chilled water temperature required. In this case it is at 46 F, which
corresponds to an absolute pressure of 0,1532 Ib per sq in. or 0.3118 in. Hg. This increases
the pumping head on the chilled water circulating pump by 14.7 — 0.15 = 14.55 Ib per
square inch, or 33.5 ft. The total pumping head is, therefore, 75.0 + 33.5 = 108.5 ft.
1200 gpm X 8.34 Ib per gallon X 108.5 ft head
33,000 ft-lb X 0.75 pump efficiency " P'
43.7 bhp X 0.746 X 1200 hr AQ Qnn . ,
- ~-x^ - - - -SE~~' - = 48,800 kwhr.
0.80 motor efficiency
The total power required by the auxiliary equipment is
93,300 + 48,800 = 142,100 kwhr.
The 142,100 kwhr at 2 cents per kwhr will cost $2,842
The cost of the steam, from Question 5, is 1,929
The total annual power cost, using a steam ejector system, is $4,771
These calculations indicate that for the assumptions made, both the dichlorodifluoro-
methane system and the steam ejector system would cost 2.6 cents per ton-hour to
operate. In order to obtain a complete analysis it would be necessary to compare the
fixed charges which include interest, depreciation, obsolescence, and maintenance.
These are customarily computed at 15 per cent of the initial cost per annum. Td this
cost must be added the cost of refrigerant make-up per year. In the steam system this
is negligible, but in the dichlorodifluoromethane system it may be approximated at
from M to % of the refrigerant charge per year.
182
Chapter 1 1
HUMIDIFICATION AND
DEHUMIDIFICATION
Air Washers* Atmospheric Water Cooling Equipment, Cooling
Towers, Design Wet-Bulb Temperature, Cooling Ponds, Natural
Draft Deck Type Towers, Mechanical Draft Towers, Winter Freezing
T71 QUIPMENT for humidifying and dehumidifying is of varied character
Py and its functions will be discussed in this chapter. An air washer is
essentially a chamber in which air is brought in intimate contact with
water, the object being (a) to wash the air or (5) to regulate the moisture
content of the air and at the same time wash it. The air comes in contact
with the water by passing it through water sprays or by passing it over
surfaces wetted by a continuous flow of water; hence the classification:
spray, scrubber, and combination spray and scrubber type washers.
A washer chamber may be constructed of wood, or stone, but it is most
often constructed of sheet metaL The lower portion of it is specially
designed as a tank to receive the water dropping through the chamber and
to serve as a reservoir from which the water may be recirculated.
It is desirable that air leaving a washer contain no water in suspension.
For this reason eliminators are provided at the washer outlet. These
may be in the form of plates or baffles upon which the free moisture is
deposited as the air is deflected through several changes from its original
direction of flow. In some washer units steel wool filter sections serve
as eliminators. However, specially designed plates are used more gener-
ally than other devices because they offer the least resistance to the flow
of air, while still performing effectively the function of free moisture
elimination. They also have the advantage of acting as scrubber surfaces
when flooded.
It is essential to uniform performance in a washer, that air enter evenly
distributed over the washer inlet, To insure this, a perforated plate or
eliminator plates are installed at the inlet. Eliminator plates are now
more generally used. They serve a second purpose in preventing the
escape of spray through the washer inlet.
Water is supplied to scrubber type units through flooding nozzles. The
capacity of these nozzles varies with the manufacturer although a fair
value of 5 gpm may be used. The nozzles are spaced on one-foot centers
across the top of the washer over the scrubber plates.
Water is supplied to spray type units through atomizing nozzles gener-
ally arranged in banks across the washer. The nozzles spray either in the
direction of the air flow, that is, downstream, or against the air flow, or
upstream. Nozzle capacities vary with the manufacturer, from 1-J^ to
2 gpm at a water pressure of about 25 Ib per square inch which pressure
183
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
is required for effective atomization. The spacing of spray nozzles is
determined by the water requirements of the particular installation. A
spray type washer may contain one, two or three banks of nozzles depend-
ing upon its application.
When an air washer is used for cleaning air it removes impurities and
dusts. In general it does not function as efficiently in this service as a
filter. For non-microscopic soluble dust its efficiency averages about
50 per cent, unless the concentration of dust is high. Its effectiveness in
removing greasy microscopic dust is practically negligible as is also its
deodorizing ability.
When a washer is used to regulate the moisture content of air it adds
moisture to (humidifies) or removes moisture from (dehumidifies) the
air to achieve the desired moisture content. (See also Chapter 3.)
When air passes through a washer wherein water is circulated without
the addition or removal of heat, the air tends to become saturated at its
entering wet-bulb temperature. What occurs here is partial or complete
adiabatic saturation. The total heat content of the air is unchanged,
inasmuch as the dry-bulb temperature of the air drops in proportion to
the amount of additional water evaporated. This action is also known as
evaporative cooling. A measure of the washer's effectiveness under these
conditions is its saturating efficiency which is equal to the drop in dry-
bulb temperature in per cent of the entering wet-bulb depression. Other
things being equal, the saturating efficiency of a spray type washer is a
function of the number of spray banks and the direction in which they
spray. The following table gives a general comparison:
3 banks — 2 upstream — 1 downstream.™ 100% saturation efficiency
2 banks — 2 upstream 95% saturation efficiency
2 banks — 1 upstream — 1 downstream 85% saturation efficiency
1 bank — upstream 80% saturation efficiency
1 bank — downstream 65% saturation efficiency
When air passes through a washer wherein the circulated water is
either cooled or heated before being returned to the spray chamber, a
heat interchange between the air and water occurs, and the air tends to
become saturated at the temperature of the leaving water. The extent
to which the leaving air and leaving water temperatures approach each
other is an index to the effectiveness of the washer under the operating
conditions. The total heat absorbed by the water in the process equals
the total heat given up by the air, or the heat given up by the water equals
the heat absorbed by the air. Depending on whether the moisture con-
tent of the air is increased or decreased during the operation, humidifi-
cation or dehumidification occurs. Heat will be added to or removed
from the air as the water supplied is of a higher or a lower temperature
than the wet-bulb temperature of the entering air.
For dehumidifiers the ratio of the difference between the leaving wet-
bulb and the leaving water .to the difference between the entering wet-
bulb and the entering ^ater may be figured as follows :
3 banks — 1 downstream — 2 upstream... 0
2 banks — 2 upstream 5
2 banks — 1 upstream — 1 downstream. 15
1 bank — upstream 20
1 bank — downstream 35
184
CHAPTER 11 — HUMIDIFICATION AND DEHUMIDIFICATION
Humidifiers may be figured on the same basis as dehumidifiers ; the
leaving water temperature, of course, will be higher than the wet-bulb
temperature of the leaving air.
The problem of cooling or heating the circulated water before returning
it to the washer chamber is external to the unit. It will suffice here to
note that heating is generally accomplished by passing the water through
closed hot water heaters or by injecting steam into the water circuit;
cooling, by passing the water through closed coolers or over refrigerating
coils in a Baudelot chamber. Often in a cooling and dehumidifiying
application, the refrigerating coils are located within the washer chamber.
SPRAY MANIFOLD
DRAIN & OVERT LOW
MANIFOLD
" DRAIN &OVCRFLOW
FIG. 1. TYPICAL SINGLE BANK AIR WASHER FIG. 2. TYPICAL Two BANK AIR WASHER
Washers are sometimes arranged in two or more stages to cool through
long ranges or to increase the over-all efficiency of heat transfer between
air and the cooling or heating medium (water, brine, etc.) . A multi-stage
washer is equivalent to a number of washers in series arrangement. Each
stage is in effect a separate washer.
Usually the catalog capacity of a washer is expressed in cubic feet of
air per minute and is based upon an air velocity of 500 feet per minute
through the gross cross-sectional area of the unit above the water level in
its tank. At this rating spray type washers handle about 2-% gpm of
water per bank per square foot of area, that is, about 5 gpm per bank per
1000 cfm. These proportions of air, water, area, and velocity may be
departed from to meet the needs of some particular job, but certain
limiting relationships should be observed. Two of the more important
items are:
185
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
a. Choose a washer for air velocities above approximately 300 fpm and below
approximately 600 fpm. Velocities outside this range are likely to result in faulty
elimination of entrained moisture.
b. When a high saturating efficiency is required, select a two or three bank spray
type unit, having a total water capacity of not less than 15 gpm per 100 cfm.
The area of a washer may be dictated by space limitations outside the
washer, such as headroom, or by space requirements inside washer, such
as face area needed by a bank of cooling coils. The length of a washer is
determined by the number of spray banks, or scrubber plates, and if
cooling coils are installed in the unit, by the number of banks of coils.
Roughly, a spray space of about 2 ft 6 in. in length is required for each
bank of sprays, (the leaving eliminators require about 1 ft 6 in., entering
eliminators about 1 ft).
The resistance to air flow through an air washer varies with the type
eliminators, number of banks of sprays, direction of spray, type of scrub-
DISTRIBUTING
THERMOMETER
DIAPHRAGM VALVE
FIG. 3. AIR WASHER WITH SPRAY WATER HEATING ARRANGEMENT
ber plates, and, if cooling coils are located in unit, by their size and type.
Washers should be selected to limit static resistances below 0.50 in.
Power Requirements
The approximate power requirement for passing 10,000 cfm of ^ air
through a humidifier of the spray type by a fan of 78 per cent mechanical
efficiency is given in Table 1, this being the fan brake horsepower for
various velocities and static pressure losses. Allowance should be made
for variations in static pressure due to the use of different diffuser plates
or inlet louvers and for variations in fan efficiencies.
ATMOSPHERIC WATER COOLING EQUIPMENT
To successfully operate a refrigerating plant or a condensing turbine,
the heat from the compressed refrigerant or the discharged steam must be
removed and dissipated. This is accomplished ordinarily by first trans-
ferring the heat of the gas to water in a heat exchanger. If the plant is
situated on the banks of a river or lake, an intake may be had upstream or
at a considerable distance from the discharge, to prevent mixing of the
heated discharged water with the inlet water. If the source of water is a
city supply or well water, the discharge water may be run into the nearest
sewer or open waterway. Lacking an unlimited water supply, or in cases
where city water is too expensive or where the water available contains
186
CHAPTER 11 — HUMIDIFICATION AND DEHUMIDIFICATION
dissolved salts which would quickly form scales on the heat-exchanging
apparatus, it is necessary to recirculate the water, and to cool it after each
passage through the heat-exchanger by exposure to air in an atmos-
pheric water cooling apparatus.
Air has a capacity for absorbing heat from water when the wet-bulb
temperature of the air is lower than the temperature of the water with
which it is in contact. The rapidity with which this transfer of heat occurs
depends upon (1) the area of water in contact with the air, (2) the relative
velocity of the air and water, and (3) the difference between the wet-bulb
temperature of the air and the temperature of the water. Because the
changes in rate do not occur in direct proportion to changes in the govern-
ing factors, data on the performance of atmospheric water cooling equip-
ment are largely empirical.
TABLE 1. APPROXIMATE FAN BRAKE HORSEPOWER
Requirements for passing 10,000 cfm of air through humidifiers at various velocities and static pressures.
Mechanical efficiency of fan — 78 per cent.
30 DEG ELIMINATORS SPACED
45 DEG ELIMINATORS SPACED
VELOCITY
ON 1-Ys
IN. CENTERS
ON 2-}4 IN. CENTERS
Static Pressure
!
Static Pressure
In. Water
In. Water
500
0.20
I 0.40
0.40
0.80
550
0.24
| 0.48
0.48
0.97
600 ! 0.29
i 0.58
0.58
1.15
650 0.34
• i 0.68
0.68
1.35
As the heat content of the air increases, its wet-bulb temperature rises.
(See Chapter 1.) Because it is impractical to leave the air in contact
with water for a long enough time to permit the wet-bulb temperature of
the air and the temperature of the water to reach equilibrium, atmos-
pheric water cooling equipment aims to circulate only enough air to cool
the water to the desired temperature with the least possible expenditure
of power.
Cooling Towers
In an air washer, humidifier or dehumidifier, the air is first conditioned
by water to change its moisture and temperature, and it is then sent to
the place where it is to be used. In water cooling equipment the tem-
perature of the water is reduced by air, and the cooled water is carried to
its point of usage. In the air washer, an excess of water is used to con-
dition a fixed quantity of air, while in water cooling equipment, an excess
quantity of air is used to cool a fixed quantity of water.
Both* types of equipment have a common basis of design, however, in
that the size of the equipment is determined by the quantity of air that
must be handled. With the air washer, the size of the equipment is fixed
by the quantity of air to be conditioned, and the amount of conditioning
is controlled by the quantity and temperature of the water supplied and
its method of application. With water cooling apparatus, its size and the
quantity of air required bear no direct relation to the quantity of water
being cooled, but vary through a wide range for different services and
conditions.
187
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Sizes of Equipment
Assuming a definite quantity of water to be cooled, the size and design
of atmospheric cooling equipment are affected by the following factors:
L Temperature range through which the water must be cooled.
2. Number of degrees above the wet-bulb temperature of the entering air to which
the water temperature must be reduced.
3. Temperature of the atmospheric wet-bulb at which the required cooling must be
performed.
4. Time of contact of the air with the water. (This involves height or length of the
apparatus and velocity of air.)
5. Surface of water exposed to each unit quantity of air.
6. Relative velocity of air and water.
TABLE 2. CONDENSER DESIGN DATA
GAS
MAXIMUM PRESSURE
DESIRED IN
CONDENSER
GAS TEMPERATURE
IN CONDENSEH
F
LEAVING HOT WATER TEMPERATURE
F
Best Design
Average Design
Steam
28 in. vacuum
99.7
114.3
126.0
96.0
86.0
100.0
100.0
97
110
120
92
83
96
96
93
105
114
88
81
92
93
Steam
27 in. vacuum
Steam
26 in. vacuum
Ammonia
185 Ib gage
head pressure
1030 Ib gage
head pressure
102 Ib gage
head pressure
1171bgage
head pressure
Carbon dioxide..
Methyl^
chloride
Dichlorodi-
fluoromethane
Items 1, 2, and 3 are established by the type of service and geographical
location, while items 4, 5, and 6 depend upon the design of the equipment.
The establishment of a proper cooling range depends upon :
1. Type of service (refrigerating, internal combustion engine and steam condensing).
2. Wet-bulb temperature at which the equipment must operate satisfactorily.
3. Type of condenser or heat-exchanger used.
Because the design of an entire plant is usually affected by the quantity
and temperature of the cooling water supply, plants should be designed
for cooling water conditions which can be most efficiently attained. The
first consideration is usually the limiting temperature of the plant. For
example, if an ammonia compressor refrigerating plant is to be designed
for 185 Ib head pressure as a normal maximum, the limiting temperature
of the ammonia in the condenser is 96 F. Should the ammonia temperature
go above this figure the head pressure will exceed 185 Ib and power con-
sumption increases. To obtain this head pressure, the temperature of the
circulating water leaving the condenser must always be less than 96 F
by an amount depending upon the size and design of the condenser, the
quantity of water being circulated, and the refrigerating tonnage being
produced. A condenser having a large surface per ton of refrigeration
may be designed to operate satisfactorily with the leaving hot water
temperature within 3 deg or 4 deg of the ammonia temperature cor-
responding to the head pressure, while a small condenser might require
a 10 deg difference.
188
CHAPTER 11 — HUMIDIFICATION AND DEHUMIDIFICATION
Table 2 lists several gases with data as to the temperatures and pres-
sures for which commercial condensers are designed. Internal combustion
engines have limiting hot water temperatures of 125 F to 140 F. The
cooling of such fluids as milk or wort has variable requirements and is
usually done in counter-flow heat-exchangers in which the leaving circu-
lating water is at a much higher temperature than is the leaving fluid.
The temperature range, once the hot water temperature is approxi-
mately known, depends upon:
1. Maximum wet-bulb temperature at which the full quantity of heat must be
dissipated.
2. Efficiency of the atmospheric cooling equipment considered.
Design Wet- Bulb Temperatures
The maximum wet-bulb temperature at which the full quantity of
water must be cooled through the entire range is never, in commercial
design, the maximum wet-bulb temperature ever known to exist at the
location nor the average wet-bulb temperature over any period. The
former basis would require atmospheric cooling equipment several times
greater than normal size, and the latter would result during a large part of
the time, in higher condenser water temperatures than those for which the
plant was designed. For instance, the maximum wet-bulb temperature
recorded in New York City is 88 F, and the July noon average for 64
years is close to 68 F. Yet in the years 1925 to 1931, inclusive, there were
but 6 hrs per year when the wet-bulb temperature reached 80 F or more,
and there were 975 hours in the average summer (June to September,
inclusive) when the wet-bulb temperature was 68 F or above. As these
975 hours represent a third of the summer period, cooling equipment
based upon the noon average July wet-bulb of 68 F would be inadequate.
Commercial practice is to choose a wet-bulb temperature for refrigeration
design purposes which is not exceeded during more than 5 to 8 per cent
of the summer hours (75 F for New York City), with somewhat lower
requirements for steam turbines and internal combustion engines. This
difference is made because the heaviest load on a refrigerating plant is
coincident with high wet-bulb temperatures, whereas the heaviest electric
power demand occurs either in the winter or after nightfall in summer,
when the wet-bulb temperature is low. Table 1, Chapter 8, shows safe
design wet-bulb temperatures which will not be exceeded more than 8 per
cent of the time in an average summer.
Knowing the hot water temperature and the wet-bulb temperature for
which the equipment must be designed, the cold water temperature must
be chosen to place the requirement within the efficiency range of the type
of atmospheric water cooling apparatus to be used. Efficiency of atmos-
pheric water cooling apparatus is expressed as the percentage ratio of the
actual cooling range to the possible cooling range. Since the wet-bulb
temperature of the entering air is the lowest temperature to which the
water could possibly be cooled this is :
Percentage cooling efficiency of atmospheric water cooling equipment =
(hot water temperature — cold water temperature ) X 100
hot water temperature — wet-bulb temperature of entering air
189
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Efficiencies of various types of atmospheric water cooling apparatus
vary through wide limits, depending upon air velocity, concentration of
water per square foot of area, and the type of equipment. The commercial
range of efficiencies is given in Table 3 although unusual designs may
operate outside these ranges.
From consideration of the factors which include the cooling range and
design wet-bulb temperature, the quantity of water required can be
calculated from the amount of heat to be dissipated. The normal amounts
of heat to be removed from various parts of the cooling equipment are:
Compressor refrigeration 220 to 270 Btu per minute per ton
Condenser turbine 950 to 980 Btu per pound of steam
Steam jet refrigerating appartus 1030 to 1150 Btu per pound of steam
Diesel engine 2800 to 4500 Btu per horsepower
Cooling Ponds
A natural pond is often used as a source of condensing water. The
hot water should be discharged close to the surface at the shore line, as
natural air movement over the surface of the water will cause evaporation
TABLE 3. EFFICIENCY OF ATMOSPHERIC WATER COOLING EQUIPMENT
EQUIPMENT
COOLING EFFICIENCY— PEH CENT
MjnJ.mi.TTn.
Usual
Maximum
Spray Ponds
30
45 to 55
60
Spray Towers
40
45 to 55
60
Natural Draft Deck or Atmospheric
Towers
35
50 to 70
90
Mechanical Draft
35
55 to 75
90
and carry away heat. Because increased density due to the loss of heat
causes the cooled water to sink to the bottom of the pond, the suction
connection for intake water should be placed as far below the surface as
possible, and at as great a distance from the discharge as practicable.
Spray Cooling Ponds
*
The spray pond consists of a basin, above which nozzles are located to
spray water up into the air. Properly designed spray nozzles break up the
water into small drops, but not into a mist because the individual drops
must be heavy enough to fall back into the basin and not drift off. The
water surface exposed to the air for cooling is the combined area of all the
small drops. Since the rate of heat removal by atmospheric water cooling
is a function of the area of water exposed to the air, the difference in
temperature between the water and the wet-bulb temperature of the air,
the relative velocity of air and water, and the duration of contact of the
air with the water, a much larger quantity of heat may be dissipated in a
given area with the spray pond than with the cooling pond, because of (1)
the speed with which the drops travel as they are propelled into the air
and fall back into the water basin, (2) the increased wind velocity at a
point above the surrounding structures or terrain, (3) the increased
190
CHAPTER 1 1 — HUMIDIFICATJON AND DEHUMIDIFICATION
volume of air used, and (4) the vastly increased area of contact between
air and water.
Spray pond efficiencies are increased by (1) elevating the nozzles to a
higher point above the surface of the water in the basin, (2) increasing the
spacing between nozzles of any one capacity, (3) using smaller capacity
nozzles, to decrease the concentration of water per unit area, and (4)
using smaller nozzles and increasing the pressure to maintain the same
concentration of water per unit area. Usual practice is to locate the
nozzles from 3 ft to 6 ft above the edge of the basin, to supply from 5 Ib to
12 Ib pressure at the nozzles, using nozzles spraying from 20 gpm to
60 gpm each and spacing them so the average water delivered to the
surface of the pond is from 0.1 gpm per square foot in a small pond to
0.8 gpm per square foot in a large pond.
Increasing the pressure, spacing the nozzles farther apart, or increasing
the elevation of the nozzles will increase the cross-section of spray cloud
exposed to the air, and therefore increase the quantity of air coming in
contact with the water. Best results are obtained by placing the nozzles
in a long relatively narrow area located broadside to the wind.
Spray ponds may be located on the ground if they have an earthen or
a concrete basin, or they may be placed on roofs having special waterproof
roofing. To prevent excessive drift loss, or the carrying of entrained
water beyond the edge of the pond by the air on the leeward side, louver
fences are required for roof locations and for those ground locations where
space is so restricted that the outer nozzles cannot be located at least
20 ft to 25 ft from the edge of the basin. Such fences usually are con-
structed of horizontal louvers overlapping so the air is forced to turn a
corner in passing through the fence, and the heavier drops of water are
thrown back, owing to their inertia. The louvers also restrict the flow of
air, particularly at the higher wind velocities, and thus further reduce the
possibility of water being carried off. The height of an effective fence
should be equal to the height of the spray cloud. Louver boards are
preferably of red gulf cypress or California redwood supported on cast-
iron, steel or wood posts, Where building ordinances forbid the use of
combustible materials, sheet metal is customarily used.
Algae formations may be a considerable nuisance in a spray pond.
Such growths are killed by the periodic addition of potassium permanga-
nate to the pond water. Addition of the dissolved chemical should be
made until the water holds a faint pink color for at least 15 min.
Spray Cooling Towers
Where not more than 30,000 Btu per minute are to be dissipated, the
spray cooling tower is a satisfactory apparatus. The word tower in this
connection is somewhat of a misnomer as the apparatus is essentially a
narrow spVay pond with a high louver fence. As usually built, the nozzles
spray down from the top of the structure and the distance from the center
of the nozzle system to the fence on either side is not more than half the
distance that the nozzles are elevated above the water basin. Heights
range from 6 ft to 15 ft and the total width of a structure is not usually
greater than its height. Spray cooling towers occupy less space on small
jobs than spray ponds of equivalent capacities because the towers have
a capacity of from 0.6 gpm to 1.5 gpm per square foot of tower area. The
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
louvers are continually wet, and so add to the surface of water exposed
to the cooling air.
Natural Draft Deck Type Towers
In past years most of the atmospheric water cooling on refrigeration
work has been done with natural draft deck type towers, which are also
referred to as wind or atmospheric towers. These towers consist of heavy
wooden or steel framework from 15 ft to 80 ft high and from 6 ft to 30 ft
wide, having open horizontal lattice-work platforms or decks at regular
intervals from top to bottom, and a catch basin at the foot. The hot
water is distributed over the upper part of the structure by means of
troughs, splash heads, or nozzles, and it drips from deck to deck down to
the basin. The object of the decks is to arrest the fall of the water so as to
present efficient cooling surfaces to the air, which passes through the
tower parallel to the decks. The decks also add to the area of water
surface exposed to the air, but since they furnish a resistance to air flow,
too many decks are a detriment.
To prevent the loss of water on the leeward side of the tower, wide
splash boards are attached at regular intervals from top to bottom. These
boards or louvers extend outward and upward, and in most designs the
top edge of each louver extends above the bottom edge of the one above it.
Efficiency of a deck tower is improved, within limits, by increased
height, increased length, or increased width, The first two increase the
area of water exposed to the wind, and the latter increases the time of
contact of the air with the water.
Wind Velocities on Natural Draft Equipment
Since natural air movement is the prime requirement for a deck type
tower, spray cooling tower, or spray pond, the apparatus must be de-
signed to produce the desired cooling on days when the wind velocity is
below average when the wet-bulb temperature is at the maximum chosen
for design, and when the plant is operating at full load. The apparatus
must also, for best results, be located with its longest axis at right angles
to the direction of the prevailing hot weather breeze. Table 1 Chapter 8,
gives the average summer wind velocities and directions in representative
cities. Natural draft cooling equipment should be designed to operate
properly with not more than one-half of the average wind velocity, and in
no case should it need a wind velocity of more than 5 mph. It is obvious
that natural draft towers and other natural draft equipment must be so
located that they are not obstructed by trees, buildings, or other wind
deflectors.
Mechanical Draft Towers
Mechanical draft towers usually consist of vertical shells, constructed
of wood, metal, or masonry, in which water is distributed uniformly at the
top and falls to a collecting basin at the bottom. The inside of the tower
may be filled with wood checker-work over which the water drips, or the
water surface may be presented to the air by filling the entire inside of the
structure with spray from nozzles. Air is circulated through the tower
from bottom to top by forced or induced draft fans. Since the air flows
counter to the water, the air is in contact with the hottest of the water
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CHAPTER 11 — HUMIDIFICATION AND DEHUMIDIFICATION
just before leaving the top of the tower, and each unit of air picks up more
heat than a similar unit would on natural draft equipment, so the me-
chanical draft tower cools water by using less air than the other types of
equipment need. As movement of the air through the towers is obtained
by power-consuming fans, it is essential that the air used be reduced to a
minimum so as to secure the lowest possible operating cost.
The efficiency of a mechanical draft tower is increased by increasing
height, area, or air quantity. Increasing the height increases the length
of time the air is in contact with the water without affecting seriously the
fan power required, but it increases the pumping power needed. In-
creasing the area while maintaining constant fan power increases the air
quantity somewhat and because of louvered velocities it increases the
time this air is in contact with the water. The surface area of water in
contact with the air is increased in both cases. Increasing the air quantity
decreases the time the air is in contact with the water, but, since a greater
quantity is passing through, the average differential between the water
temperature and the wet-bulb temperature of the air is increased, and
this speeds up the heat transfer rate. Increased air quantities are
obtained only at the expense of increased fan power, which increases
approximately as the cube of the air quantity. Air velocities through
mechanical draft towers vary from 250 f pm to 600 f pm over the gross area
of the structure.
Mechanical draft water cooling equipment may be set up inside build-
ings, where it usually draws its air supply from the general space in which
it is installed, and discharges its exhaust air through a duct to the outside.
Indoor cooling towers may be either of the wood-filled or the spray-filled
type. In many cases where little height but considerable area is available,
water is cooled in a spray-filled structure similar to an air washer, with
the air passing horizontally through the apparatus and being discharged
through a duct to the outside. Such apparatus does not have the counter
flow advantage of the vertical mechanical draft water cooling equipment,
and therefore requires a much larger excess of air for proper operation.
Air velocities and operating powers are considerably above those required
by vertical mechanical draft water cooling equipment.
Make-up Water
Since the atmospheric water cooling equipment performs its functions
chiefly by evaporating a portion of the water in order to cool the re-
mainder, there is a continual drain on the quantity of water in the system,
and this loss must be replaced. Approximately 1 gal of water is lost for
every 1000 gal of water cooled per degree of cooling range; so if 1000 gpm
of water are cooled through a 10 deg range, 10 gpm of water will be re-
quired to replace evaporated water. Replacement supply is usually
regulated by a float control valve. Because the evaporation of the water
leaves behind the salts which the water contained, high concentration of
salts may make chemical treatment of the make-up water necessary to
avoid excessive deposits in the condensers.
Winter Freezing
If atmospheric water cooling equipment is operated in freezing weather,
the water may be cooled below freezing temperature so ice forms and
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
collects until its weight causes damage. To obviate freezing during con-
tinued operation, the efficiency of the apparatus may be lowered. This
is done on the spray pond and the spray cooling tower by reducing the
quantity of water fed to the apparatus, thereby lowering the pressure at
the nozzles and increasing the size of the drops produced. On the deck
TABLE 4. COMPARISON OF VARIOUS TYPES OF ATMOSPHERIC WATER COOLING EQUIPMENT
Figures indicate order of desirability
COOLING
POND
SPRAY
POND
SPRAY
TOWER
DECK
TOWER
MECHANICAL
DRAFT
INDOOR
TOWEH
Cost
X
2
1
3
4
5
Area
5
4
3
2
1
X
Height
1
2
3
4-5
4-5
X
Weight per sq ft
X
X
1
3
4
2
Independence of wind velocitv
6
3
4
5
1-2
1-2
Drift nuisance
1
6
5
4
2-3
2-3
Make-up water required
1
6
5
4
2-3
2-3
Pumping head
1
2
3
4-5
4-5
6
Maintenance .
2
1
3
4
5
6
Suitability for congested districts
X
5
4
3
1
2
Water quantity required for definite
result
6
5
4
1-2
1-2
3
*Not comparable.
tower the upper system may be shut off and a secondary distribution
system put in service midway down the height of the tower. The water
will be kept above freezing because it will have shorter contact with the
air. The mechanical draft tower can be protected by reducing the air
flow through the tower, by stopping or reducing the speed of the fans, or
by partially closing dampers.
If the system is operated intermittently in freezing weather, water in
the basin may freeze and the expansion of the ice may do harm. Freezing
during intermittent operation can be prevented only by draining the
water basin when it is out of service. On small roof installations, a tank
large enough to hold all the water in the system is often installed inside
the building and the basin is drained into this by gravity, the pump suc-
tion being taken from this inside tank.
A comparison of various types of water cooling equipment is given in
Table 4.
PROBLEMS IN PRACTICE
1 • What three systems of humidification are used in textile, printing, and
lithographic plants?
a. Indirect: Introduction of moistened air into the rooms.
b. Direct: Spraying of moisture into the rooms.
c. Combined: Direct and indirect as above.
2 • How may relative humidity be controlled?
a. If constant room temperature is to be maintained:
1. To maintain a constant relative humidity, the dew point must be kept constant.
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CHAPTER 11 — HUMIDIFICATION AND DEHUMIDIFICATION
2. To increase the relative humidity, the dew point must be raised.
3. To decrease the relative humidity, the dew point must be lowered.
b. If constant dew point is to be maintained:
1. To maintain a constant relative humidity, the room temperature must remain
constant.
2. To increase the relative humidity, the room temperature must be lowered.
3. To decrease the relative humidity, the room temperature must be raised.
c. With varying dew-point temperatures:
1. To maintain a constant relative humidity, the room temperature must vary
directly and in almost equal amount with the dew point.
2. To increase the relative humidity, the difference between room temperature and
dew point must be decreased.
3. To decrease the relative humidity, the difference between room temperature and
dew point must be increased.
d. With varying room temperatures:
1. To maintain a constant relative humidity, the dew point must vary directly and in
almost equal amount with the room temperature.
2. To increase the relative humidity, the difference between dew point and room
temperature must be decreased.
3. To decrease the relative humidity, the difference between dewr point and room
temperature must be increased.
3 • In industrial air conditioning plants, what are the four sources of heat
which must be taken into consideration in the design of a system?
a. Heat transfer from the outside air.
b. Body heat from employees.
c. Sun effect.
d. Heat equivalent of power consumed in driving machinery, in lighting, and in manu-
facturing processes in general.
4 • Why do cooling towers give best results when the humidity of the air is low?
The cooling of water by dropping it through air depends mostly upon the evaporation of
the water. If the relative humidity of the air is low, the water vapor will be readily
absorbed and carried away, while if the humidity of the air is high, its capacity to pick
up water vapor is less and the water is cooled less with the same exposure to air.
5 • What performance tests should be given air washers?
a. Capacity.
b. Resistance.
c. Visible entrainment of free moisture.
d. Humidifying efficiency.
e. Cleaning effect.
6 • What are the several different types of water-cooling towers?
a. Those with forced draft.
b. Those with natural draft open to the atmosphere.
c. Those with natural draft closed to the atmosphere.
d. Those with combined natural and forced draft.
7 • What are the different types of air washers?
a. Spray, b. Wet scrubber, c. Combination spray and scrubber.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
8 • What is the saturation efficiency for an air washer with the common
variations in spray arrangement?
For three banks, two up-stream and one down-stream .. 100C<
For two banks, both up-stream - -. 95r^
For two banks, one up-stream and one down -stream , 85 %
For one bank, up-stream 80^
For one bank, down-stream., . .. ,, 65^r
9 • Upon what air velocity are air washers usually rated?
500 fpm, through the area above the tank.
10 • What wet-bulb temperature for the outside air is usually selected in air
conditioning design when cooling is to be accomplished?
One which is not exceeded more than 5 to 8 per cent of the time in the locality where the
plant is to be situated.
11 • Where should the suction connection be placed in a cooling pond?
As far below the surface as possible and as far away from the discharge as practicable
12 • What chemical is used to kill algae formations in spray ponds?
Potassium permanganate.
13 • What is the usual amount of spray water delivered to a cooling pond per
square foot of pond area?
From 0.1 gpm on small sizes to 0,8 gpm on large sizes.
14 • What is the usual amount of water delivered in cooling towers per squar
foot of area?
From 0.6 to 1.5 gpm.
15 • About how much water is lost by evaporation in atmospheric cooling?
About 1 gal per 1000 gal for each degree of cooling range.
16 • How is freezing obviated in cooling pond sprays?
The pressure and quantity of water is lowered so that the drops become of increased size
and do not freeze so readily.
17 • What is the cause of a high concentration of salts in the cooling water of
an atmospherically cooled system?
The constant evaporation of a small portion of the water leaves salts behind to accumu-
late in the unevaporated water.
196
Chapter 12
UNIT AIR CONDITIONERS AND
CONDITIONING SYSTEMS
Definition, Advantages and Uses, Functions, Sources of Refrigera-
tion and Heat, Types and Locations, Construction of Apparatus.,
Installation., Basis of Equipment Ratings, Calculation of Required
Capacity, Approximate Costs
A IR conditioning systems fall into two general types known as the unit
jC\, type and the central type. A unit air conditioner is an assembly of
parts, such as fans, humidifiers, coils, controls, and other equipment,
which form a complete unit at the point of manufacture. This usually
restricts the size of the unit to a capacity below 10,000 cfm. With the
unit conditioner, the performance is the responsibility of the manu-
facturer. This is in contradistinction to a central air conditioning system
which may produce the same results but for which the various parts are
purchased separately and assembled by the contractor on the job, who
guarantees the performance of the assembled system.
Unit Air Conditioner
A unit air conditioner generally has a capacity less than 30,000 Btu per
hour for cooling, or 60,000 Btu per hour for heating, to make it suitable
for the space to be conditioned. If it does not provide simultaneous
control of at least four of the recognized functions of air conditioning (see,
p. 201) the apparatus should be classified as a unit heater or unit venti-
lator (Chapter 13) or as a unit cooler, a humidifier, or a window-type
ventilator.
The apparatus, instead of being wholly self-contained, may depend
upon separately located parts piped to supply heating, cooling, or humi-
difying mediums to the unit. A duct may supply outdoor air for circu-
lation, but ducts are seldom used for air discharge and recirculation.
When the term unit conditioner is applied to such set-ups as the com-
bination of a filter and a fan in a housing to be used with gravity warm air
furnaces, or to humidifiers and heating coils to be used with steam or hot-
water boilers to comprise a unified central air conditioning plant, the
usage of the term is inaccurate; such devices may be designated as
accessory units, but this leads to confusion. However, since such accessory
equipment is used, a description and discussion of its several types are
given in the next few paragraphs before the main topic of this chapter,
unit heaters, is taken up.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Accessory Central Fan Conditioning Apparatus
This Includes every kind of equipment constituting an accessory to an
existing or new system for warm air heating service, and also certain
forms of conditioning equipment used with hot water or steam boilers in
residential service. Some of these accessories provide only a fan and an
air filter, while others include humidifying and cooling functions. The
performance of such equipment is influenced by the outside temperature
and humidity; the conditions surrounding the house or apartment, such
as construction and exposure to sun ; the type of heating system to which
the apparatus is attached; and the location of the device on the heating
system. Many of these installations are of limited_capacity and effective-
ness ; conservative manufacturers will be discriminating in their claims
for added comfort from the use of such equipment, depending on its
design and functions.
i * Ml --ll-^K— — .A,r to p00m&
FIG. 1. FURNACE ACCESSORY UNIT
A feature of the fan-and-filter accessory unit is its availability ^ for
ventilation in summer; it makes possible a rapid cooling in the evening,
after the outdoor air temperature has dropped below that of the rooms.
If the fan is large enough completely to change the air in the building
served every two or three minutes, the effect will be similar to that from
so-called attic fans, (see Chapter 13), with the important advantage that
the air is filtered. Fans of smaller capacity, proportioned only for ^the
winter heating duty, may also provide an appreciable measure of cooling.
Another advantage is improved headroom in the basements of residences,
obtainable by substituting horizontal ducts for those of comparatively
steep pitch necessary when gravity air circulation is depended upon. A
fan-and-filter accessory using a dry-mat type of filter, applied to a warm
air furnace, is shown in Fig. 1.
A more elaborate unit (Fig. 2), for use with a hot water heating boiler
provides heating, humidification, filtering, and positive air circulation in
winter; the heating coil may be used also in summer with mechanical
refrigeration or for circulating city water or chilled water from an ice tank,
to provide cooling and dehumidification. The disposition of fans, the
cloth filter of bag design, the spray type humidifier, as well as noise
198
CHAPTER 12 — UNIT AIR CONDITIONERS AND CONDITIONING SYSTEMS
elimination features comprising canvas collars at the fan outlets and
rubber pads under the fan bedplate, are indicated in Fig. 3. The use of a
single element for both winter and summer functions tends to reduce the
first cost, although it adds some complications in piping.
Another assembly of air conditioning equipment with a standard
heating furnace, in this instance burning gas to provide warm air, is
shown in Fig. 4. The apparatus comprises an air filter, a motor-driven
fan, and an air washer. No refrigeration is used with this equipment.
Hot Water
Better
.ftir to ffooms
•Fitter
Fan
FIG. 2. UNIT WITH HOT WATER BOILER
Rubbe,
Pads,
FIG. 3.
HEATING AND COOLING UNIT
WITH CLOTH FILTER
Return tfir from
-/?/r Wisher
' Furnace
FIG. 4. GAS FIRED FURNACE UNIT
For oil fuel, the unit shown in Fig. 5 can be installed to obtain filtered,
warmed, and humidified air. An oil burner and a heat exchanger provide
the heat. A cooling section may be inserted between the fan and the heat
exchanger, cold water being circulated through the cooling element. For
automatic control, a room thermostat is provided to start the oil burner
whenever the temperature falls. The rising temperature in the heat
exchanger causes a second thermostat to start the fan. As soon as the
temperature in the house rises to normal, the room thermostat shuts down
the oil burner and operates the thermostat controlling the fan.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Having disposed of the accessory central fan conditioning apparatus,
the balance of this chapter will concern only the unit air conditioner as
defined in Chapter 41.
ADVANTAGES AND USES OF UNIT AIR CONDITIONERS
Unit air conditioners are suitable for commercial and comfort applica-
tions because they permit installation without seriously disturbing the
building occupants, and they allow rearrangement or a change in capacity
to suit changed requirements occasioned by new tenants. Tenants may
even furnish their own installations and remove the apparatus from the
premises at the expiration of their leases. In some types of buildings, the
installation costs are lower for unit conditioners than those for central fan
systems, and costs are further lowered in that there is no need for space in
which to house a conditioning plant. The choice between unit and
To Room,
FIG. 5. OIL FIRED UNIT
central systems will, in many instances, require a close study of instal-
lation conditions at the site, and a preparation of comparative cost
estimates, in addition to a consideration of the more intangible factors.
Industrial Uses
The origin of the unit conditioner, like that of air conditioning itself,
was in the industrial field for maintaining desired atmospheric conditions
in rooms or sections of manufacturing plants where structural limitations
or service requirements made a central system uneconomic. Industrial
applications continue to offer an important market for unit conditioners,
in bakeries, candy factories, drug-manufacturing plants, laboratories,
produce-storage rooms, printing plants, and similar places.
Commercial Uses
The most active field for unit conditioners at the present time is in
commercial establishments, such as barber and beauty shops, funeral
parlors, retail and specialty stores, and small restaurants, where increased
patronage or larger purchases per customer offer economic justification of
first cost and operating expense.
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CHAPTER 12 — UNIT AIR CONDITIONERS AND CONDITIONING SYSTEMS
The air-handling units installed overhead in Pullman cars, diners and
coaches, in the middle or at the ends of the cars which discharge the air
horizontally at the ceiling level, are essentially unit conditioners. How-
ever, because of special construction to meet space limitations and other
requirements, they are unsuitable for general use and are not further
discussed.
Personal Uses
The major recent development in the air conditioning industry has been
in new and improved types of unit conditioners suitable for apartments,
homes, hotel rooms, and offices. These uses demand apparatus that is
compact, of unobtrusive appearance and in harmony with the room
finish and furnishings, quiet in operation, automatic, and reliable.
As with all new major appliances for the home, problems of relatively
high first cost, of comparatively rapid obsolescence and of operating
expense demand the continuous close attention of manufacturers and of
others interested in developing the potential market. Unit conditioners
are still distinctly in the pioneering stage where such problems must be
met and solved if development — especially of residential units — is to
proceed as fast as it should. Public understanding of residential air con-
ditioning still requires cultivation in order to cBspel fears of possible
excessive operating costs and of possible high obsolescence due from
frequent model changes. Progress in this direction is being helped by the
increasing efforts of manufacturing companies which are now spending
large sums to insure sound promotion of unit conditioners. Likewise, the
National Better-Housing Program inaugurated in 1934 is likely to prove of
real value to the air conditioning industry and to accelerate greatly the
rate of public acceptance and installation of unit conditioners.
FUNCTIONS OF UNIT CONDITIONERS
Unit air conditioners may be classified as the all-year unit, the summer
unit, and the winter unit. The all-year unit performs all of the functions
of an air conditioning system ; namely , cooling, dehumidification, heating,
humidification, air circulation, air cleaning — with or without a supply of
fresh air — and a simultaneous control of all functions. The summer unit
must provide cooling, dehumidification, air circulation, and air cleaning;
the winter unit must provide heating, humidification, air circulation, and
air cleaning. Either of these seasonal-use units may or may not provide a
fresh air supply and a simultaneous control of the functions.
In some instances, winter-type units equipped with filters for air
cleaning and with fresh air connections may be operated in summer for
ventilation, but the system cannot then properly be said to provide
all year conditioning. It is important that the features and limitations of
the specific apparatus be carefully explained to a prospective user, so that
disappointments and complaints concerning operating results may be
avoided.
The functions listed are performed by the unit conditioners offered by
different manufacturers in various ways, some of which appear in the
following outline. See the next few pages for more detailed explanations
of cooling and heating theories and methods.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
1. Cooling:
By coils, usually of finned type, for direct expansion of refrigerant from a self-
contained unit or from a remotely-located compressor.
By coils, of finned type, for brine or cold water from separate refrigeration plant,
or for cool water from city mains, private wells, or an ice water tank.
By water sprays.
By passage of air over ice cakes.
2. Dehumidification :
By lowering the air temperature below the dew point, using any of the devices
outlined for cooling.
By adsorption materials, such as silica gel or activated alumina.
3. Heating:
By coils, usually of finned type, for steam or hot water from system distribution
mains.
By electric heating elements.
By gas burners.
4. Humidification:
By evaporating or entraining water by an air current, from wetted surfaces or
water sprays.
5. Air circulation :
By motor-driven fans which discharge air into room at points, in directions and
with velocities that insure adequate ventilation without drafts; air discharge
usually through top, at a slight angle from vertical.
6. Air cleaning:
By mechanical filters.
By water washing with sprays.
By water washing by contact with condensation or by trickling water on cooling
coils or a mesh cell.
7. Fresh air supply:
By air connection from outdoors, usually through adjustable window ducts at
rear of housing, with mixing dampers for control of volume of recirculated room
air taken in through louvers at each end.
8. Control:
By manual adjustment or automatic regulation, by thermostats or hygrostats.
SOURCES OF REFRIGERATION
Mechanical Refrigeration — Direct and Indirect
In general, mechanical refrigeration uses the low-temperature evapora-
tion of a liquid to absorb heat in a set of coils. The resulting vapor is
restored to its original liquid state by compressing and condensing it,
abstracting the heat by passing water or air over a second set of coils at
the outlet side of the compressor. Power for compression is usually
supplied by an electric motor. The apparatus, exclusive of the evaporator
or cooling coil, is known as a condensing unit. Two methods are available
for applying mechanical refrigeration to unit conditioners.
The direct-expansion system provides for admitting the refrigerant
through a pressure reducing (expansion) valve to the cooling coil, where
its evaporation causes chilling of the surface over which the circulated air
passes. Under this method, the equipment cost is low, the refrigerant
lines need not be insulated, the apparatus is compact, and the operating
expense is minimized by the avoidance of heat leakage and by the higher
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CHAPTER 12 — UNIT Am CONDITIONERS AND CONDITIONING SYSTEMS
permissible suction pressure at the compressor inlet (as compared with
the indirect system). However, because of possible hazards from leaks,
direct expansion is usually prohibited in hospitals and places of public
assembly.
The indirect-expansion system uses a water-submerged coil in a tank
near the condensing unit, for evaporation of the refrigerant. The chilled
water or brine is then delivered under pressure by a motor-driven pump
for distribution to the cooling coils in the individual unit conditioners,
returning again to the tank. This avoids the possibility of refrigerant
vapors, whether toxic or not, leaking into the conditioned rooms. Code
•Fan Motor
•— Ha net Control
Valve
Line.
FIG. 6. ROOM COOLING UNIT
limitations on the quantity of refrigerant in the air conditioning apparatus
are overcome, and'a central condensing unit may be made to serve rooms
on different floors or in remote parts of a building, without violating
safety regulations. Difficulties that occur with compressor operation at
less than 50 per cent of rated capacity are avoided through the use of a
thermostat that shuts down the compressor when the tank water tem-
perature reaches the set minimum; operation is had at constant suction
pressure, independent of the number of unit conditioners running. With
proper choice of temperatures at which the compressor starts and stops
under thermostatic control, there is less cycling than with the direct
expansion system. Under favorable conditions, the cooling coil may be
supplied with steam or hot water for winter heating, thereby simplifying
the construction of the unit conditioner, although at the expense of some
complication in valved connections. However, the cold water tank and
circulating pump take up room, and the cost of suitably insulated dis-
tribution piping is greater than that of equivalent liquid lines and suction
returns for a direct-expansion system.
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Separate Condensing Units
The separate condensing unit, for mechanical refrigeration with unit
conditioners that are not self-contained, comprises the assembly, on a
bedplate, of a compactly arranged compressor with motor, drive, con-
denser, liquid receiver, and automatic controls. The cylinder jacket of
the compressor and the condenser may be cooled with water under pres-
sure, or with air supplied by a fan mounted integrally with the compressor.
A condensing unit connected to a single unit conditioner is shown in
Fig. 6.
Steam-Jet Apparatus
Stearn-jet (vacuum) refrigeration may be used in localities served by
district steam mains, or in buildings with boiler plants available for
summer use. While avoiding power-driven compressors, the steam-jet
apparatus requires an appreciable amount of power for auxiliary pumps,
and an increased quantity of cooling water to absorb the heat from the
motive steam in addition to that abstracted from the conditioned rooms.
Most installations of this type are of large capacity — above 20 tons
refrigeration — but recently developed equipment is available for instal-
lations as small as 2 to 5 tons.
City or Well Water
Systems installed near the Great Lakes or in other regions where low
cost cooling water is available in summer may often use this water
directly in the coils of air conditioning units. In certain other places, well
water can be obtained in sufficient quantity at moderate pumping
expense. Restrictions on bulk use of water, or on discharge of large
volumes into the sanitary sewers may prevent direct cooling.
Ice
Two methods of using ice are applicable : direct, with air circulated by a
fan over ice cakes in an insulated tank within the room served; indirect,
with an ice-melting tank remote from the unit conditioners, circulating
chilled water to coils in the units by means of a motor-driven pump. The
direct method has been employed with portable room coolers for hotel
guest rooms, hospitals, and residences, where the demand for air con-
ditioning is moderate and variable with respect to rooms served from day
to day, and where it is feasible to move the units into a service room or
kitchen for emptying and icing. The indirect method is identical with
that common in theaters using ice, except that the water after spraying
over the ice is pumped to unit conditioners instead of to a central fan
system.
SOURCES OF HEAT
Steam or Hot Water Coils
The heating coils of unit conditioners for all-year or winter service are
available for either steam or hot water, supplied at low or high pressure
from building heating plants. Because the relatively high Btu per hour
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CHAPTER 12 — UNIT AIR CONDITIONERS AND CONDITIONING SYSTEMS
outputs for heating (usually 1.5 to 3 times the rate for cooling), under
thermostatic control, may produce disturbances in small heating systems,
it is usually necessary that two-pipe steam systems operate at all times
above atmospheric pressure, and that hot water systems have forced
circulation with a pump. Unless the room space occupied by radiators
in an existing building is needed for the unit conditioners or for other
purposes, it is preferable that some or all of them be retained, so that the
unit conditioners need supply only sufficient heat to permit their satis-
factory operation for humidification.
Electric Elements or Gas Burners
Where energy is available at low cost, electric heating elements may be
used in place of steam or hot water coils for winter service. Evaporation
of water for winter humidification may likewise be accomplished electri-
cally. More uniform control of temperature and humidity is practicable
with electricity, because the heating elements may be divided into sections
separately connected through thermostatically controlled switches.
However, wiring connections must be larger than needed for summer
conditioning with a compressor built into the unit; for instance, the
power for a unit rated at 24,000 Btu per hour for winter heating is about
seven times that used for 12,000 Btu per hour of summer cooling by the
same unit.
A new unit conditioner employing the adsorption method for summer
dehumidification is fitted with gas burners for winter heating. A part of
the humidification is supplied by the water vapor resulting from com-
bustion of hydrogen in the gas fuel, and the remainder by evaporation
from a heated- water receptacle.
TYPES AND LOCATIONS OF UNIT CONDITIONERS
Fixed
The majority of unit conditioners are designed for floor mounting,
preferably under windows. However, when radiators for winter heating
occupy the window space and it is not desired to shift them or to eliminate
them by using all-year type floor units, the location may be against
interior partitions or alongside permanently situated furniture. In all
cases care must be taken to insure that the direction of the air discharge
will not cause drafts that may be objectionable to occupants. When out-
door air for ventilation is taken through the unit, the under-window
position is advantageous, since it permits using a short inlet duct from
louvers in a filler panel permanently inserted beneath the raised lower
sash.
Ceiling or wall-mounted units may be used in commercial establish-
ments, when floor space is at a premium. They generally secure refri-
geration from a remotely placed condensing unit and are designed for
support by means of hanger rods. It is often possible to conceal them in
adjoining closets or workrooms, with the air discharge louvers fixed in the
intervening wall ; this makes it easy also to conceal the piping connections
and wiring. In stores, suspended type units may conveniently be placed
over the housed-in show windows.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Portable
Portable summer-function units mounted on rubber-tired casters or
rollers can be obtained in the smaller capacities up to about 9000 Btu per
hour. They may have built-in compressor units using city water for
jacket and condenser cooling, or they may employ ice or low temperature
city water. Hose connections for water supply and return, and for con-
densate drains, are needed in addition to a plug-in electrical connection.
It is expected that a market for such units can be developed in hospitals,
hotel guest rooms, and residences.
Special Types of Units
The field for unit conditioners has been extended by the appearance of
small low-cost devices for comfort cooling that localize the cooling effect
to the immediate vicinity of the user. These include bed tents and robe-
type coolers, which require motors not larger than J^ hp. The tent is
suspended from a bracket attached to the bed frame, and the cooler
placed alongside is connected to it with a short collar for the air discharge.
The robe-type device is intended for barber and beauty shops; it works
on the same principle. Besides handling much smaller quantities of air,
these expedients achieve economy because they operate only when
required for the comfort of the user.
Reversed Refrigeration Heating
All-year unit conditioners that utilize their refrigeration apparatus for
winter heating by the principle known as reverse refrigeration cycle, are
being developed. A detailed explanation of this system is given in
Chapter 39. For regions rarely having winter temperatures below
freezing, there is believed to be a considerable field of application for such
equipment. The heat delivered to the room will range between 2.5 and
3.5 times the equivalent of the electrical power taken by the motor,
depending on the outdoor temperature. The gain is, of course, derived
from the ambient air, requiring an inlet and an outlet duct for passing a
considerable volume. Lower rates for energy may sometimes be obtained,
under the resulting improved annual load factor, when both cooling and
heating are provided electrically.
LOCATION OF UNITS, AIR FLOW PATHS
The number of units, the availability of space, and the convenience of
making piping, wiring, and duct connections, which involves the location
of outside cooling, heating, and power sources, must be considered in
choosing locations for the units, as must the positions of persons, furni-
ture, and materials in the space to be conditioned, and the requirements
of air distribution.
The most important of these considerations is air distribution, and units
should be so located as to secure uniformity in all parts of the room
whether the application is for comfort conditioning or for industrial uses.
The discharge of cooled air, in general, should be upward immediately at
the conditioner, with sufficient horizontal component to carry to the most
remote point; return to the inlet of the unit, which occurs below the
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CHAPTER 12 — UNIT AIR CONDITIONERS AND CONDITIONING SYSTEMS
breathing line and along the floor, should be at low velocity. The location
of doorways, air vents, and sources of heat should be studied, as they have
a marked effect on air flow and on temperature uniformity. Infiltration
through leaky windows with certain wind directions likewise disturbs or
restricts the circulation of air from the unit conditioner, and frequently
causes cold spots by preventing diffusion at the ceiling. Velocities below
the breathing line should be kept low — not over 40 to 70 feet per minute ;
in this range, an anemometer will not work, and the Kata thermometer
must be used for testing purposes.
CONSTRUCTION OF APPARATUS
Description of Typical Units
The types and designs of air conditioning units proposed or in produc-
tion are legion ; new designs are constantly appearing, with a tendency
toward better mechanical construction and a wider range of application.
However, nearly all types now commercially available utilize mechanical
refrigeration or cold water for summer cooling, and consequently the
descriptions below are limited to such equipment, using electric power.
Illustrations of current makes and models will be found in the Catalog
Data Section of this volume.
Fig. 7 shows an all-year, floor- type unit for direct expansion of re-
frigerant supplied by a remotely located compressor; with modifications,
the cooling coil can be used with chilled water. The fans below the
separate cooling and heating elements deliver the air against deflectors
that give distribution across the element face, and the usual drip pan for
condensation is provided. Separate elements for heating and for cooling
possess the advantage of allowing the former to be connected to the
source of heat with piping entirely separate from the refrigerant lines to
the cooling element, with no cross-connections. Thus the unit may be
used for warming in the morning and for cooling later in the day, if
desired, without manipulation of valves. When this unit is installed for
cooling only, the heating element is omitted.
A summer-function unit with fans above the cooling element is shown
in Fig. 6; a condensing unit, with schematic diagram of refrigerant piping
and wiring, is included. This air conditioning unit, as well as that in
Fig. 7, when housed in an ornamental cabinet, is suitable for high grade
residential or commercial installations.
An entirely different arrangement, shown in Fig. 8, places both the air
inlet and the discharge at the top of the unit. The fan in the upper
portion at one side discharges the air toward the bottom, where it turns
and passes horizontally through an air washer equipped with atomizing
sprays. The path continues vertically upward through eliminators,
cooling surface, and heating surface before leaving the unit. With steam
or hot water connected to the heating element, tempered water to the
sprays, and refrigerated water to the cooling element, this unit gives con-
trolled temperature, humidity, air cleaning and air movement in both
summer and winter. Air washing may be continued in summer to
remove room odors'. Acoustical treatment of the housing and the outlet
baffles permits installation where the noise requirements are exacting.
One of the most recently developed units, designed particularly for low
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
cost installations, is shown in Fig.9. The twin fans with wheels, mounted
on extensions of the motor shaft, take air from the floor and send it
downward through a passage containing a water spray. The direction of
flow is then reversed, the air passing through a double set of coils for
cooling or heating, and leaving the cabinet through a top grille. The
FIG. 7. FLOOR UNIT FOR HEATING AND COOLING
7"o ffo om
\ \ \ \ t tt
FIG. 8. UNIT WITH TOP INLET AND OUTLET
spray nozzles are supplied with city water, the excess collecting in the air
reversal chamber, which has a drain. The cooling coil uses water from
the city mains or other low- temperature source; alternatively, direct
expansion of refrigerant from a motor-driven condensing unit can be
utilized. The unit provides all-year functions, the cleaning being accom-
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CHAPTER 12 — UNIT AIR CONDITIONERS AND CONDITIONING SYSTEMS
plished by the spray in winter and by contact with the wetted cooling coil
in summer. Automatic electrically operated controls for water flow,
steam flow, temperature, and humidity are optional. «.
For industrial applications, the floor-type unit, Fig. 10, or the ceiling-
type, Fig. 11, may be used. The former has a galvanized steel casing that
encloses the cooling and heating elements, with fans mounted above them ;
the air discharges from the top through 90-degree elbow ducts, which
deliver it in a nearly horizontal direction. The operating motor for the
fan is carried on a bracket at one side, and at the bottom a condensate
drip pan is provided ; space between the pan and motor bracket is utilized
•Outlets
FIG. 10. INDUSTRIAL FLOOR TYPE
FIG. 9. ALL-YEAR TYPE UNIT
CONDITIONER
for traps and valves. This unit does not wash or filter the air, nor is a
fresh-air supply provided for ventilation; thus only cooling, dehumidi-
fication, and circulation can be accomplished in summer, and heating and
circulation in winter.
The ceiling type, Fig. 11, is primarily for summer use, although when
supplemented by a regular heating system it can accomplish a limited
amount of humidifying in winter. The apparatus consists of an air washer
with the usual water sprays, eliminator plates, and air circulating fan,
designed for suspension from the ceiling. The air supply is taken from
the room through the intake register, passes through the water spray and
eliminators, and is delivered back into the room through the discharge
outlet equipped with adjustable lowers. The refrigeration unit may be
treated at any convenient point and tiie cooled water circulated to and
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
from the conditioner through pipes at the ceiling, so that no floor space is
lost. This style of unit is for industrial and large office installations.
Where the appearance on the ceiling is objectionable, the unit may be
placed at some other location, using a compact duct system for the air to
and from the conditioning unit.
In the following paragraphs, typical forms of construction are outlined.
Many variations of these have been used, and modifications or entirely
new details are constantly being introduced. The^ Catalog Data Section
illustrates and describes the current designs of leading equipment manu-
facturers.
Cabinets, Registers
Cabinets are made of furniture grade sheet steel suitable for pressing in
panels, protected by corrosion-resistant priming coatings. The design is
such as to permit access to the equipment, which is independently sup-
ported on a frame or chassis. Heat insulation of either rigid or flexible
Eliminators
Intake.
Fein
-Pra/n
FIG. 11. SUMMER COOLING UNIT
Chamber
type, to prevent sweating in summer or overheating in winter, is used,
particularly with thermostatic controls that start and stop the fans
without affecting the supply of heating or cooling medium to the coils.
Sound-deadening is equally important, to avoid vibration or drumming
effect of the panels. The finish of commercial and residential units is
usually in imitation of wood grain, or may be in solid color to harmonize
with room finish and furnishings.
Outlet registers are generally placed in the top of the cabinet to direct
the air at an angle approximately 30 degrees from the vertical^ They
should be proportioned to maintain sufficiently high air velocity for
preventing a local cold spot caused by too short a flow circuit in the room.
Types that give ejector action, entraining some room air and propelling
the mixture a considerable distance away from the unit, are preferred.
Return-rair registers should act as sound-deadeners and serve to hide the
internal mechanism.
Motors
Motors are usually of the capacitor or repulsion-induction types, single-
phase. However, in sizes 5 hp and larger, three-phase will ordinarily -be
preferable; this will deperid on character and capacity of service facilities
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CHAPTER 12 — UNIT AIR CONDITIONERS AND CONDITIONING SYSTEMS
available. Special designs giving low starting current, silent running and
(in the case of compressor motors) high starting torque, are essential.
Features to minimize lamp flicker and radio interference must be incor-
porated. coordinated with characteristics of the compressor. For auto-
matically controlled units, two motors (with sequence relay for con-
secutive starting) are sometimes direct-connected to the load, for holding
the current inrush to a low value, when the starting torque of the driven
equipment permits. Devices known as suction unloaders, permitting
large air or refrigeration compressors to come up to speed without load,
involve too much complication for the size of apparatus used with unit
conditioners.
Refrigerants
The choice of refrigerants for a direct-expansion system is limited to
non-toxic, nearly odorless fluids — principally methyl chloride, freon or
iso-butane. Local ordinances and fire regulations prescribe the maximum
quantity of refrigerant in a system for residential and usual commercial
requirements. Indirect systems may use ammonia, sulphur dioxide or
carbon dioxide, since the equipment and piping can then be isolated,
remote from the conditioned rooms.
Compressors, Condensers, Cooling Coils or Evaporators
Compressors of the multi-cylinder reciprocating or rotary designs are
preferred, as they minimize starting troubles and lamp flicker. Gland or
shaft-seal leaks, with freon or methyl chloride, must be provided against,
because of the difficulty in detecting leaks before the refrigerant charge is
lost ; this is especially important when the pressure in the crankcase tends
to rise after the compressor shuts down. V-belt drives from motors permit
the compressor and motor each to run at its most economical speed, and
provide desirable resilience at the instant of starting.
Condensers for water cooling are of either the double-tube or shell-and-
tube types, with the latter preferred when the water carries dissolved or
suspended solids; provision for opening and cleaning should be made.
Air cooled condensers usually are supplied with air by propeller fans
integral with the compressor flywheels or mounted on the compressor
shafts.
Evaporator coils, in units using direct expansion of the refrigerant, also
constitute the cooling coils over which the air flows to be cooled and
dehumidified. They are constructed of metal suitable for the refrigerant
used, and have fijis-oa the exterior to increase the heat transfer per unit
length of tube. The arrangement and amount of surface provided, in
relation to the maintained refrigerant temperature, the^initial tempera-
ture and dew point of the air, and the rate of air circulation over the coil
determine the final air temperature and thus the amount of debumidj-
fication secured. With, indirect refrigerating systems, the cooling fcoifo in
the units are usually somewhat larger, because the cooling fluid (water or
brine) is at a higher ialet temperature; the evaporator in this case is
remotely located (with tibe <x>acbn^ia^ unit) and serves to chil the water
circulated by a pump ta, the cofeia £he mnit^o^dit^i^rs>
<m coo&ig mis weqtares & drip pan, with
f disposal: f>efati tfiefc fibteBj&by .^jter^ryr^iriationsy or an
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
ejector operated from the city water supply used for winter humidi-
fication or for cooling the condenser. In some cases, a condensate storage
tank to be emptied manually, or a motor-driven pump, is supplied.
Eliminator baffles may be provided immediately below the outlet grille to
intercept any drops of water picked up by the air current.
Humidifiers
Humidification in unit conditioners may be accomplished by sprays
using cold or heated water at city main pressure, or by water trickling
over heated surfaces or a mesh filling. The design must provide for sup-
plying the heat of evaporation, and for exposing to the air current a
sufficient area of water film. This requires a considerable excess of water,
which may be wasted to a drain or recirculated by a pump ; with the latter,
periodic flushing of the system must be practicable, to dispose of the dirt
removed from the air. When considerable amounts of fresh air are
provided by the unit conditioner or enter by infiltration, the quantity of
water to maintain the desired humidity is greater than when the unit
merely recirculates and the room has only moderate leakage. In the
latter case the humidifier can be small, since only a slight amount of
moisture is supplied to the air with each passage through the unit.
Fans, Fresh Air Supply
Fans are usually of the centrifugal type with scrolls, inlet cones, blades,
and tip speeds designed for quiet operation. Compactness and uniform
distribution of air across the width of the coils and grilles are obtained by
using two or more fans in parallel, the rotors mounted on a common shaft
or on a double-end extension of the motor shaft. Housings and deflectors
(if used at the fan outlets) may be acoustically treated. Propeller-type
fans are sometimes used, although more difficult to make quiet. Efficiency
is a secondary consideration, because the motors are of small fractional-
horsepower sizes.
Fresh air supply connections are usually through a fixed panel inserted
in a window frame between sill and lower sash; this has a louvered and
screened opening, connected with a metal duct to the space in the cabinet
at the inlet side of the fans. A manually adjustable damper regulates the
proportionate volumes of recirculated and fresh air.
Filters
Air cleaning devices include filters of glass or metal wool, cellulose, felt,
or woven fabric; they are usually of the renewable cartridge type, designed
for low air resistance. Types especially effective in the removal of hay
fever pollen are desirable. An alternative device is a water spray also
serving as a humidifier in winter, or when supplied with chilled water, as
a cooler and dehumidifier in summer. The fins on cooling coils, auto-
matically wetted by condensate obtained in dehumidifying the air, are
also employed in some types. Complete removal of tobacco smoke is not
possible with any type of filter or washer used in unit conditioners ; the
limited amount of ventilation air in summer, admissible from the oper-
ating cost standpoint, often results in a smoke haze. The only remedy is
increased ventilation, with consequent higher operating expense; the air
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CHAPTER 12 — UNIT AIR CONDITIONERS AND CONDITIONING SYSTEMS
outlets should be near the ceiling, to tap the upper stratum where the
smoke is most dense.
Heating Coifs
Heating coils are generally of the extended-surface type for compact-
ness, and may be designed for any pressure of steam available, or for
forced circulation hot water — usually about 180 F. Some types of heating
systems, both hot water and steam, are unsuited to unit conditioners,
especially when thermostatically controlled, because of the resulting
sudden changes in load. Gravity-circulation hot water systems must be
converted to forced circulation, if unit conditioners are to be connected,
and steam systems must always operate at pressures above atmosphere.
Manual and Automatic Controls
Manual control is generally used with unit conditioners, because of the
high cost of reliable automatic controls. Fan and compressor motors are
started and stopped by individual switches. Fluids for the heating and
cooling coils are regulated with manual valves, generally permitting the
flow to continue regardless of whether the fan is operating; with this
arrangement, adequate heat insulation must be provided within the
cabinet, and the size of the unit conditioner in a room is limited to that
which will give the minimum required heat supply by gravity air circu-
lation through the conditioner when the fan is stopped.
Automatic controls consist of a thermostat for room temperature and a
hygrostat for humidity. The former starts and stops the fan in the unit
conditioner, thereby controlling the supply of cooled or warmed air to the
room. A hygrostat is not usually supplied, because of high cost and
imperfect reliability of types now available ; when used, it is connected to
the valve admitting water to a spray- or trickle-type humidifier, or to a
refrigerant supply valve controlling a supplementary section of the cooling
coil. The best arrangement is one that permits the full capacity of the
compressor to be utilized for either sensible heat removal or dehumidi-
fication, based on the principle that the compressor capacity varies
approximately as the temperature of the refrigerant in the cooling coil.
Compressors are started and stopped by pressure switches on the dis-
charge (high pressure) side. Water supply to the compressor jackets and
the compressor is turned on and off by a solenoid valve energized when
the compressor motor starts. Refrigerant supply to the cooling coil
(constituting the evaporator) is usually regulated by a thermostatic valve,
as a function of the refrigerant outlet temperature, or by a flow valve that
tends to hold a constant level in the liquid receiver.
INSTALLATION OF UNIT CONDITIONERS
Piping, Wiring, Ducts
Piping connections for water and steam are made preferably with
corrosion resisting material, usually brass or copper. Light weight rigid
tubing with sweated joint fittings has advantages over threaded construc-
tion. Flexible copper tubing with compression type connections may be
used in the smaller sizes (u>f> to % in. dra.), as it lends itself to conceal-
ment In existing walls of other places difficult of access ; distribution of the
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
refrigerant from a remotely located condensing unit is usually made with
such flexible tubing.
Wiring connections should be made using modern materials and
methods, such as will receive approval of local inspection authorities
having jurisdiction. For portable conditioning units with built-in com-
pressors, particular care should be taken to select rugged receptacles and
plugs; waterproof flexible cords are recommended because of the pos-
sibility of water leakage from adjacent hose connections or by overflow
from the unit if the drain becomes stopped.
Ducts for outgoing air supply, usually from nearby window openings,
present no particular problems.
Workmanship
The requirements as to workmanship for installation of unit con-
ditioners are exceptionally severe; this is particularly true for work in
high grade offices and residences, in occupied quarters. Handling of the
materials and the cutting, patching, and refinishing invariably demand
neatness, accuracy, and planning that the ordinary mechanic is un-
familiar with, so that close supervision must be given.
BASIS OF EQUIPMENT RATINGS1
While no uniform standard for rating unit air conditioners has yet been
adopted, manufacturers generally give a definite rating for each size unit,
based on the volume of air handled by the fan for cooling; the rating is
stated in Btu per hour at a given dry- and wet-bulb temperature of air
entering the unit, with a given refrigerant temperature maintained within
the coil, resulting in a stated relationship between sensible and latent heat
removal. The temperature of the cooling water or air supply for the
condensing unit is also involved. The duty for heating service is likewise
given in Btu per hour with 70 F room temperature, for a stated steam
pressure or hot water temperature (usually 180 F) . Humidifying capacity
is based on hourly weight of water evaporated. The Catalog Data Section
in this volume gives the ratings of current models offered by leading
manufacturers.
METHODS OF CALCULATING REQUIRED CAPACITY
In estimating the load for unit air conditioning apparatus, a survey
should be made of the surrounding conditions and the heat quantities
calculated. The climatic conditions representing the maximum loads to
be designed for should be carefully determined.
Cooling Loads
For cooling loads served by unit conditioners, the factors for heat gains
and losses are the same as apply to central fan systems. The sensible
heat gains are from the following sources:
iRefer to the standard ratings of air conditioning equipment of the National Electric Manufactures
Association.
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CHAPTER 12 — UNIT AIR CONDITIONERS AND CONDITIONING SYSTEMS
a. Sun effect.
b. Transmission through walls, floors, ceilings, glass, and roofs.
c. Infiltration, including ventilation air.
d. People.
e. Lights.
/. Electric motors and appliances.
g. Steam and gas appliances.
h. Miscellaneous heat sources.
The latent heat load, usually determined separately, comes from
dehumidification of the air and from people and materials. The method
and factors to be used are outlined in standard texts and in manufacturers*
handbooks.
Rated capacity for direct-expansion refrigeration units should include
an allowance for the heat equivalent of the fan-motor input, plus the
portion of the power to the compressor not removed by the cooling water.
For indirect-expansion systems, allowance should be made for heat
pickup by the refrigerant circulating lines, or for the pickup by a chilled-
water or brine-storage tank and for the shaft-horsepower input to a
circulating pump, if used.
As a rough approximation, the refrigeration tonnage required for unit
conditioners serving rooms devoted to various uses may be assumed as
follows :
TYPES OF ROOMS
CTT FT PER TON
Cafeterias, lunchrooms
1000 to 1500
Barber and beauty shops, dance halls
1200 to 1800
Dining rooms, crowded retail stores
1500 to 2000
Theaters
1800 to 2400
General offices, club rooms, retail stores, funeral parlors
2000 to 3000
Banks, brokers' offices, private offices, residences
2500 to 4000
Obviously, there will be many cases to which the mentioned limiting
values do not apply, A calculation of the cooling load, based on an
accurate survey, should always be made before recommending the size of
an installation or naming a cost figure.
Heating Loads
Heating loads are calculated in the usual manner, as outlined in
Chapter 7. Allowance must be made also for the latent heat supplied to
the water for humidification, when the infiltration or ventilation air
quantity is large.
APPROXIMATE COSTS
Equipment and Installation
Floor type all-year, unit conditioners, oon^pletely self-e6ntaiaed and
equipped with motor-<Mve0 ^compressors and iiN&rm^t^tie controls,
' at the
, in-
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
eluding expense for piping, wiring and fresh-air ducts, amounting to
between 175 and $150, with perhaps $50 additional if overtime work is
necessary to avoid inconveniencing the occupants of offices or other
quarters.
A similar unit without compressor, using chilled water or direct-
expansion refrigerant from a remotely located compressor, costs $175 or
more at the factory. Installation expense is somewhat greater than for
the self-contained unit, because the refrigerant piping costs more than is
saved by the reduction in wiring. Omission of the heating coil, confining
the unit to summer functions only, lowers the price by $25 to $100.
For smaller units, rated between 6000 and 8000 Btu per hour,*providing
all-year service and equipped with motor-driven compressors, the price
ranges from $325 to $450 at the factory. Larger units, rated at about
24,000 Btu per hour for cooling, cost between 25 and 45 per cent more
than the 12,000-Btu per hour size. Delivery and installation expense
for either of these sizes does not differ more than 25 per cent from that
of the 12,000-Btu per hour unit.
Industrial- type conditioners, either floor or suspended models, are
usually made only in ratings of 20,000 Btu per hour and higher; omission
of expensively finished cabinets and other differences reduces the cost con-
siderably below that of corresponding sizes of commercial and residential
types.
Condensing units completely assembled on bedplates, especially
adapted to serve one or more unit conditioners, are available. They com-
prise a motor, compressor, condenser, liquid receiver, and control devices,
and they are arranged for water cooling or are equipped (in the smaller
sizes) with fans for air cooling. Prices for representative sizes, including
motors but not starting equipment, are as follows:
BTU PER HOUR
FACTORY PRICE
INSTALLATION COST
8,000
12,000
36,000
60,000
120,000
$275 and up
325 and up
575 and up
800 and up
1100 and up
$60 and up
65 and up
80 and up
90 and up
125 and lip
These prices are for water-cooled types; air cooling adds $25 to
Installation cost includes transportation, foundations, wiring, starting
equipment, cooling water piping or air ducts, and sound-deadening
insulation. Refrigerant connections from liquid receiver and compressor
suction to unit conditioners are not included. For office buildings and
similar occupied quarters, overtime labor may increase the cost.
The prices given represent net cost to the ultimate purchaser. Although
roughly indicative of the present-day market, they should not be used as
a basis of a specific estimate or an appropriation, because designs, ratings,
and prices vary considerably between makers and in different parts of the
country. Transportation and installation expense is even more variable,
depending upon freight rates, wage scales, and particularly on the con-
dition of the building and the adequacy of existing piping and wiring
systems to which the unit conditioners are to be connected. Furthermore,
216
CHAPTER 12 — UNIT AIR CONDITIONERS AND CONDITIONING SYSTEMS
the industry is in a state of fairly rapid development, so that any general
cost figures should be used with caution.
Operation
For a 24,000-Btu per hour unit operating at full load for summer
cooling, with electricity at §0.05 per kwh and 70 F city water at $1.50
per 1000 cu ft, the hourly electric and water expense works out to $0.14.
Under climatic conditions representative of a large part of the country,
the load factor, during the 10 hours' daily operation required, averages
50 per cent; this gives a daily operating cost of $0.70. The seasonal cost
for localities requiring, for example, 1000 hours of operation (at 50 per
cent load factor) then becomes $70. To this should be added main-
tenance and fixed charges of 25 per cent (based on about a five-year useful
life) on an investment around $1200. The over-all expense for owning and
operating is thus of the order of $370 per year. Such a cost may be
incurred, in a climate like that of New York City, by the owner of a home
in which at least the living room, the dining room, and a bedroom are
cooled with unit conditioners served by refrigerating equipment of the
mentioned capacity.
This expense may be compared with the cost of winter heating, com-
puted by adding annual fixed and maintenance charges to cost of fuel,
attendance, and other items. The comfort attainable in hot, humid
weather is so welcome that these costs will undoubtedly be looked upon as
reasonable by an increasing number of people, as they become personally
familiar with the value of the service rendered by modern air conditioning
equipment. Exposure to such comfort in commercial establishments,
railroad trains, and other public places will unquestionably tend to
increase the demand for home installations at a greater rate each year.
The developments in equipment for the type of service described have
been rapid during the past few years and the latest models may be seen
in the Catalog Data Section.
PROBLEMS IN PRACTICE
1 • Are unit conditioners necessarily self-contained?
No. The heating medium is always supplied from a separate plant, and the refrigerant
for cooling and dehumidification may come from a separately located compressor or
other supply source.
2 0 Are ducts used with unit conditioners?
Yes. Usually a short connection for fresh air intake is made to an adjacent window
or wall opening. Occasionally ducts are required for return air and for discharge, when a
unit is located near the room served but not within it.
3 • What is the meaning of the term condensing unit in relation to unit air
conditioners?
A condensing unit is the assembly, on a bedplate, of a compactly arranged refrigeration
compressor, motor, drive, condenser, liquid receiver, and automatic controls used for
supplying the refrigeration.
217
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
4 • Why are metal surface cooling elements instead of liquid spray chambers
used in the design of most unit air conditioners and unit coolers?
The first cost of the surface cooling type of unit is considerably less than the cost of
spray type equipment. Further, the requirements of many industrial air conditioning
jobs and of all comfort cooling jobs where unit equipment is applicable can often be
effectively met with the use of surface type units, with a reduction in the jspace required
for making the installation. Where space conditions are especially limited, the cross-
sectional area of the surface cooler can be reduced because the resulting increase in
velocity over the coil surface increases the effectiveness of the ^ surface, whereas an
increase in velocity through a liquid spray would reduce its effectiveness.
5 • Why are air conditioning units with metal cooling surfaces not desirable
for all industrial jobs?
Wherever unusually close control of relative humidity is required, a spray type unit will
prove to be more "satisfactory. Relative humidity control and accurate temperature
control, however, can be maintained without difficulty with the use of metal surface
units.
6 • Why is accurate control of relative humidity with surface coolers more or
less complicated?
A surface cooler cannot add moisture to the air, and moisture is removed only when the
surface temperature is below the entering dew-point temperature. Any change in
condition of the entering air will result in a change in the dry-bulb depression of the
leaving air. This change in entering condition requires not only a readjustment of the
air volume but also a change in the coil temperature, if accurate control over the relative
humidity is to be maintained.
7 • What in general are the characteristics of unit conditioner operation
using surface coils?
For a constant entering dry-bulb temperature and a constant refrigerant temperature
any increase in the entering wet-bulb temperature will produce a rise in the leaving dry-
bulb temperature with an accompanying reduction in the wet-bulb depression of the
leaving air. The sensible heat removed by the unit decreases and the latent heat in-
creases, while the total heat removed also increases. When the dry-bulb temperature of
entering air is increased, with constant refrigerant temperature and constant wet-bulb
temperature of entering air, the wet-bulb depression of the leaving air increases, and
since it is this depression which determines the maintained relative humidity it must be
carefully considered when selecting the unit.
8 • If a drop in the dry -bulb temperature of entering air reduces the capacity
of the unit, is there not danger of selecting a unit which is too small, if its
selection should be based on an excessive entering dry-bulb temperature?
Yes. If the total cooling load is largely internal (such as from occupants and lights) as
distinguished from the cooling load of outdoor air, and the unit is selected on the basis
of a too high dry-bulb temperature of entering air, then, in the event of under capacity,
it might be possible to maintain the room temperature by reducing the quantity of out-
door air. But this increases the recirculated air taken into the unit, reducing the dry-
bulb temperature of entering air and, therefore, reducing the sensible heat capacity of
the unit. This reduction in capacity may offset the gain obtained by reducing the
amount of outdoor air taken in. Further, since the total tonnage required for any instal-
lation is equal to the total internal heat load plus the total heat removed from the out-
door air, and since the outdoor air might have a wet-bulb temperature equal to the
designed wet-bulb but less than the designed dry-bulb temperature, then the sensible
heat capacity of the unit will be less than that required. It follows that unit air con-
ditioners and coolers should not be selected on a basis of the maximum possible dry-bulb
temperature of entering air.
218
Chapter 13
UNIT HE ATKKS. VENTILATORS,
AND COOLERS
Types of Unit Heaters, Heating Media, Entering and Delivery-
Temperature, Output of Unit Heaters, Direction of Discharge,
Boiler Capacity, Direct-Fired Units, Unit Ventilators, Split and
Combined Systems, Location of Unit Ventilators, Capacities,
Attic Fans, Unit Coolers
A UN IT heater consists of the combination of a heating element and a
fan or blower having a common enclosure, and placed within or
adjacent to the space to be heated. Generally, no ducts are attached to
the inlets or outlets. A unit ventilator is similar in principle of operation
to a unit heater, but is designed to use all or part outdoor air with or
without alternate provision for handling recirculated air. Unit heaters
are designed mainly for factory and industrial use, whereas unit venti-
lators are intended largely for school and office ventilation and heating.
Unit heaters and unit ventilators are designed to :
1 . Circulate the air in the building at a rapid rate.
2. Reduce the temperature differential between floor and ceiling.
3. Direct the heated air so as to accomplish the positive and rapid placing of the
heat where it is effective.
4. Remove the cold stratum of air from the floor.
TYPES OF UNITS
There are many types of unit heaters available. Most of them employ
convectors to be supplied with steam or hot water. Some are mounted on
the floor, whereas others are designed for suspension overhead. Heating
surfaces in the form of steel pipe coils, non-ferrous tubes or shapes with
extended surfaces, cast-iron, and pressed and built-up sections of the
cartridge or automotive type are all used in unit heater construction.
Among the unit heaters available are types designed especially . for
industrial purposes having from one to four warm air outlets per heater
which may be arranged to discharge in selected directions and which will
project their heating effects over distances of from 30 to 200 ft from the
heater, depending upon the capacity of the heater and upon the design of
the fan and outlets. Because these heaters have been satisfactory when
placed as far as 400 ft from each other, it is possible to select the heater
location best suited to the production layout in factories. There are
available propeller fan type heaters of smaller capacity with outlet
velocities of from 300 to 800 fpm, and these may be placed from 30 to
100 ft apart.
219
AMERICAN SOCIETY o/ HEATING and VENTILATING ENGINEERS GUIDE, 1935
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220
CHAPTER 13 — UNIT HEATERS, VENTILATORS, AND COOLERS
HEATING MEDIA
The convectors in unit heaters or ventilators may be supplied with
either hot water or steam. When water is used, it should be circulated
mechanically, and the pumpage rate and friction loss should be based
upon test data from the particular unit to be employed. The heat output
of a given heater will be less when using water than with steam, even at
the same temperature.
Either high or low pressure steam may be used, but the proper venting
of air and the prevention of flash steam from the condensate in the
returns become increasingly troublesome as the steam pressure increases.
The use of properly constructed traps with some reliable form of ther-
mostatic air by-pass solves the first of these problems, while proper
venting or the use of condensing legs solves the second. Increasing the
return temperature tends to increase return line corrosion, especially at
points where overheated condensate or steam are led into a line.
When low pressure steam is used with unit heaters and ventilating
units it is highly important that proper means be provided for taking care
of the heavy condensation. They should not be applied to low pressure
gravity return systems except where the difference between the heater
level and the boiler water line is large enough to compensate for the
pressure loss through the convector at its highest possible condensation
rate. The use of vacuum or return pumps and receivers is advisable,
with jobs of any considerable size, as the surest way of taking care of
condensate and at the same time providing for proper venting of the
units directly into a vacuum return line system, or into an open vented
return system, the latter having some advantage in preventing the
formation of any vacuum in the unit itself, which sometimes tends to hold
up condensate and cause freezing.
ESTIMATING HEAT LOSSES
The heat losses of a building to be equipped with unit heaters are
determined in the same manner as for any other heating system, excepting
so far as the unit heaters may prevent air stratification and thus reduce
the temperature difference between the ceiling and floor. (See Chapter 7.)
Unit heaters may be arranged to recirculate the air or to supply warmed
air from the outside for ventilation or to make up air exhausted.
If all or a part of the air is to be taken in from out-of-doors, the heat
necessary to warm this air from the outside temperature to the inside
temperature must be added to the transmission or other losses. Units of
the number and size needed to furnish the total heat required are then
selected from the manufacturers' rating tables, using these ratings at the
steam pressure to be used and at the temperature at which the air will
enter the convector.
AIR TEMPERATURES
For recirculating heaters with intakes at the floor level, the temperature
to be maintained in the room should be used as the temperature of the air
entering the heater. Where suspended heaters are used without any
intake boxes extending down to the floor level, a higher entering air
221
AMERICAN SOCIETY of HEATING
and
VENTILATING ENGINEERS
GUIDE,
1935
TABLE 2. CONSTANTS FOR DETERMINING THE CAPACITY OF Draw-THROUGH TYPE UNIT HEATERS FOR VARIOUS STEAM PRESSURES
AND TEMPERATURES OF ENTERING AIR
(Based on Steam Pressure of 2-lb Gage and Entering Air Temperature of 60 F)
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222
CHAPTER 13 — UNIT HEATERS, VENTILATORS, AND COOLERS
temperature should be used than that at which the room is to be main-
tained. With suspended heaters taking in air at some distance above the
floor, the temperature variation from floor to ceiling may reach as much
as 1 deg for each foot of elevation during periods when the maximum
capacity of the heaters is required. Unit heaters taking in recirculated
air at the floor level should maintain -temperature differentials of less
than 0.5 deg per foot of elevation when the maximum capacity of the
heaters is required. These temperature differences per foot of elevation
are less than the corresponding variations per foot of elevation for spaces
heated by direct radiation.
Unit heaters save fuel because of their ability to circulate air at a lower
average temperature than the air circulated by direct radiators ; however,
the unit heaters must circulate more air in any given time than is needed
with direct radiators. This requires the selection of heaters having a
liberal air capacity for the required heat output, which in turn means a
relatively low final temperature. Extremely low final temperatures can
be had only at the expense of larger heaters and increased power, so that
an economic limit is imposed. In general, for heating purposes it is
advisable to use a delivery temperature not more than 70 F above the
average room temperature desired, and one considerably less where
possible.
OUTPUT OF HEATERS
It is standard practice to rate unit heaters in Btu per hour at a given
temperature of air entering the heater and at a given steam pressure
maintained in the coil. Steam at 2 Ib pressure and air entering at 60 F
are used as the standard basis of rating1. The capacity of a heater
increases as the steam pressure increases, and decreases as the entering
air temperature increases. The heat capacity for any condition of steam
pressure and entering air temperature may be calculated approximately
from any given rating by the use of factors in Tables 1 and 2. Table 1
is for blow-through and Table 2 is for draw-through unit heaters. These
tables are accurate within 5 per cent.
The ratings customarily published for unit heaters apply only for
recirculation and free discharge, unless otherwise noted in the rating
tables. If outside air intakes, filters, or ducts on the discharge side are
used with the heater, proper consideration should be given to the reduc-
tion in air and heat capacity that will result because of this added
resistance.
The percentage of this reduction in capacity will depend upon the
characteristics of the heater and on the type, design, and speed of the
fans employed, so that no specific percentage of reduction can be assigned
for all heaters for a given added resistance- In general, however, disc
or propeller fan units will have a larger reduction in capacity than housed
fan units for a given added resistance, and a given heater will have a
larger reduction in capacity as the fan speed is lowered. When confronted
with this problem the ratings under the conditions expected should be
secured from the manufacturer.
iSee A.S.H.V.E. Standard Code for Testing and Rating Steam Unit Heaters (A.S.H.V.E. TRANS-
ACTIONS, Vol. 36, 1930).
223
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
When steam supplied to the heaters contains superheat, the capacity
of the heater will be but slightly less than with saturated steam at the
same pressure. Recent tests indicate that the reduction of capacity
from this cause is negligible for superheat up to 50 deg and will not
exceed 3J^ per cent for any degree of superheat.
Heaters may be distributed through the central portions of a room
discharging toward exposed surfaces, or may be spaced around the walls,
discharging along the walls and inward as well, especially when there are
considerable roof losses.
In general, it is better to direct the discharge from the unit heaters
in such fashion that rotational circulation of the entire room content is
set up by the system rather than to have the heaters discharge at random
and in counter directions.
DIRECTION OF DISCHARGE
Various types and makes of unit heaters are illustrated in the Catalog
Section of this edition. Usually hot blasts of air in working zones are
objectionable, so heaters mounted on the floor should have their discharge
outlets above the head line and suspended heaters should be placed in
such manner and turned in such direction that the heated air stream will
not be objectionable in the working zone. In the interest of economy,
however, the elevation of the heater outlet and the direction of discharge
should be so arranged that the heated air shall be brought as close to
the head line as possible, yet not into the working zone. In general, the
higher the elevation of the unit, the greater the volume and velocity
required to bring the warm air down to the working zone, and conse-
quently, the lower the required temperature of the air leaving the unit.
BOILER CAPACITY
The capacity of the boiler should be based on the rated capacity of the
heaters at the lowest entering air temperature that will occur, plus an
allowance for line losses. Ordinarily for recirculating heaters the lowest
entering temperature will occur at the beginning of the heating period
and is usually taken as 40 F, while for ventilators taking air from outdoors
the lowest entering temperature will be the extreme outdoor temperature
expected in the district. No greater allowance in boiler capacity beyond
the calculated heat demand need be added in order to supply unit heaters
than for any other type of system.
It is unwise to install a single unit heater as the sole load on any
boiler, particularly if the unit heater motor is started and stopped by
thermostatic control. The wide and sudden fluctuations of load that
occur under such conditions would require closer attendance to the boiler
than is usually possible in a small installation. Where oil or gas is used
to fire the boiler, it is possible by means of a- pressurestat to control the
boiler, in response to this rapid fluctuation. In most cases, however, and
particularly where the boiler is coal-fired, it is advisable to use two or
more smaller heating units instead of one large unit.
Steam pressures below 5 Ib can be used with safety for recirculating
unit heaters when their coils are designed for the purpose and when
224
CHAPTER 13 — UNIT HEATERS, VENTILATORS, AND COOLERS
proper provision is made for returning the condensate. If ventilators are
to take in air that may be at a temperature below freezing, however, a
steam pressure of not less than 5 Ib should be maintained on the convector
or a corresponding differential in pressure between the supply and returns
be maintained by means of a vacuum.
QUIETNESS
In selecting unit heaters, attention should be given to the degree of
quietness required for the installation.
No given fan speed may be applied as a measure of relative quietness
to fans of different designs and proportions. Quietness is a function of
type, diameter, blade form and other variables besides speed, and all
•VACUUM BREAKER
FLOAT OR BLA3T
TRAP.
FIG. 1. UNIT HEATER CONNECTIONS
WHERE CONDENSATION Is RETURNED
TO VACUUM PUMP OR TO AN OPEN
VENTED RECEIVER
SUPPLY—
VALVES r
•AIR VENT VALVE
-WET RETURN
FIG. 2. UNIT HEATER CONNECTIONS
WHERE CONDENSATION Is RETURNED
TO BOILER THROUGH WET RETURN
these must be taken into account. In general small fans may be run at
higher motor speeds than large fans with equal quietness ; and centrifugal
fans are more easily made quiet than disc or propeller fans.
PIPING CONNECTIONS
Piping connections for unit heaters are similar to those for other types
of fan-blast heaters. Typical connections are shown in Figs. 1 and 2.
One-pipe gravity and vapor systems are not recommended for unit
heater work.
For two-pipe closed gravity return systems the return from each unit
should be fitted with a heavy-duty or blast trap, and an automatic air
valve should be connected into the return header of each unit. Pressure-
drop must be compensated for by elevation of the heater above the water
line of the boiler or of the receiver.
In pump and receiver systems the air may be eliminated by individual
air valves on the heaters, or it may be carried into the returns the same as
for vacuum systems and the entire return system be free-vented to the
225
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
atmosphere, provided all units, drip points, and radiation are properly
trapped to prevent steam entering the returns.
On vacuum or open vented systems the return from each unit should be
fitted with a large capacity trap to discharge the water of condensation
and with a thermostatic air valve for eliminating the air, or with a heavy-
duty trap for handling both the condensation and the air, provided the
air finally can be eliminated at some other point in the return system.
For high pressure systems the same kind of traps may be used as with
vacuum systems, except that they must be constructed for the pressure
used. If the air is to be eliminated at the return header of the unit, a
high pressure air valve can be used ; otherwise the air may be passed with
the condensate through the high-pressure return trap, with some danger
of return pipe corrosion and the problem of its elimination at some other
point in the system.
The connections for steam and return piping to unit heaters must
always be calculated on the basis of the high heat emission or condensation
rate of such devices. The pipe-size tables given in Chapter 32 may be
used for unit heater work by multiplying EDR values by 240 to get Btu
values.
OTHER TYPES OF UNITS
All Electric
The foregoing discussion relates generally to units in which steam or hot
water is used as the heating medium. On rare occasions electrical
resistances are used as the heating element. These are applied only where
electric power is abundant and cheap and where other forms of fuel are
scarce and expensive. (See Chapter 39.)
Direct Fired
A recent development in gas burning equipment is the direct-fired
industrial unit heater. These heaters are of the warm air type and are
equipped with fans which cause the air to pass over the heating surfaces
at a fairly high velocity and then direct the warm air in to the space to be
heated. As is the case with the steam fed unit heaters, the gas fired
appliances may be used for heating stores, shops, and warehouses. They
usually are suspended in the space to be heated and in most instances
leave the entire floor and wall area free for commercial use. Partial or
complete automatic control also may be secured on appliances of this type.
This type of heater is often used for temporary heat during building
construction or where the installation of a steam or hot water plant is for
some reason not justified.
Turbine Driven
Where high pressure steam is available it is sometimes used to drive a
steam turbine direct-connected to the unit heater. The exhaust from
this turbine, reduced in pressure, is then passed into the heating coil
where it is condensed and returned to the boiler.
INDUSTRIAL USES
In addition to their prime function of heating buildings, unit heaters
may be adapted to a number of industrial processes, such as drying
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CHAPTER 13 — UNIT HEATERS, VENTILATORS, AND COOLERS
and curing, with which the use of heated air in rapid circulation with
uniform distribution is of particular advantage. They may be used for
moisture absorption, such as fog removal in dye-houses, or for the pre-
vention of condensation on ceilings or other cold surfaces of buildings in
which process moisture is given off. When such conditions are severe, it
is necessary that the heaters draw air from outside in enough volume to
provide a rapid air change and that they operate in conjunction with
ventilators or fans for exhausting the moisture-laden air. (See discussion
of condensation in Chapter 7.)
Information on the control of unit heaters will be found in Chapter 14.
UNIT VENTILATORS2
A unit ventilator must be pleasing in design because it is generally
used where it must harmonize with the furniture or with the decorative
scheme. It consists usually of a rectangular steel cabinet finished with an
enameled surface and containing the following necessary or optional
parts:
1. Outside air inlet.
2. Inlet damper for closing the opening to the outside air inlet when the unit is not
in use.
3. Adhesive or dry type filters for cleaning the air (optional).
4. A heating element usually of special design and intended for low pressure steam.
5. Motor and fan assembly.
6. Mixing chamber where warm and cold air streams are brought together. (No
mixing chamber is normally provided where sectional type con vectors are used.)
7. Outdoor air inlet and recirculating air mixing damper (optional).
8. Device for ozonizing air (optional).
9. Discharge grille or diffuser.
10. Temperature control arrangement.
The primary functions of a unit ventilator are:
1. To supply a given quantity of outdoor air for ventilation or to mix indoor and
outdoor air.
2. To warm the air to approximately the room temperature if the unit is intended for
ventilation only, or to a higher temperature if it is intended to take care of all or a part
of the heat transmission losses from the room.
3. To control the temperature of the air delivered so as to prevent both cold drafts
and overheating.
4. To deliver air to the room in such a manner that proper distribution is obtained
without drafts.
5. To recirculate room air for the purpose of heating or promoting comfort when
ventilation is unnecessary.
6. To perform all its functions without objectionable noise.
In addition to these functions, unit ventilators frequently are arranged
so that the air supplied may be cleaned by means of filters of either the
dry or viscous type. If filters are used, the proper allowance must be
made for the Increased resistance offered to the air flow. Humidifiers in
unit ventilators are rather difficult to control and are only furnished upon
special order.
*A roof ventilator is sometimes termed a wiit ventilator*. For information on roof ventilators* see
Chapter 4.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
1. Air Supply for Ventilation. The outdoor air supply for ventilation
is delivered by motor-driven fans operated at comparatively low speeds,
the back of the cabinet being connected to the outside through rust-proof
louvers and screens. Air quantities may be estimated on the basis of data
given in Chapter 2. (See A.S.H.V.E. Ventilation Standards.)
2. Warming Incoming Air. The air is heated by passing it through
specially designed convectors. The amount of heating surface to be
provided in the unit is determined by the volume of air to be heated and
the temperature range. If the unit is to be used for supplying air for
ventilation only, the convector must be sufficient in capacity to maintain
a final air temperature of about 70 F. If the unit is to be used for heating
as well as for ventilation, the convector must be sufficient to maintain the
necessary final air temperature for the conditions involved.
3. Control of Temperature. This is accomplished by varying the tem-
perature of the air discharged from the unit (1) by the automatic opera-
tion of a mixing damper which controls the relative quantities of air
being blown through the heating unit or by-passed around it, (2) by
operation of valves on different layers of convector surfaces, or (3) by
variation in the temperature of the circulating heating medium.
The outside air inlet damper and recirculating damper (where one is
provided) should be so connected that there will be an uninterrupted
supply of air to the fans at all times the unit is in operation. These
dampers may be operated by hand or by pneumatic or electric motors
manually controlled from some central point.
These dampers may also be linked together, in the form of mixing
dampers and be controlled by a thermostat in the cold air intake, by a
differential thermostat acted upon by both the cold air and the recircu-
lated air, or by a thermostat in the two streams of air after they are
mixed, so as to keep the relative proportion of air taken in from out-of-
doors commensurate with outside temperatures and to prevent drafts of
cold air being blown through the unit into the room.
Provision should be made for the inlet damper to close automatically
whenever the fans are shut down, and not to open until^ the room is
properly heated when the fans are again started. The minimum tem-
perature of the air delivered by the machine should be regulated auto-
matically by a thermostat in the outlet air which controls the temperature
of the heated convector, or this minimum temperature may be main-
tained by properly mixing the inside and outside air by means of the
mixing dampers under thermostatic control referred to above. Another
thermostat in the recirculated air intake to the unit or elsewhere in the
room controls by-pass dampers or the supply of heating medium, or^both,
so as to control the temperature of the air leaving the unit according to
the heat requirements of the room. In addition to these thermostats, a
room thermostat is needed to control any other heat sources for the
room. (See Chapter 14.)
Thermostats for controlling by-pass dampers must ^be of the inter-
mediate type to hold the dampers in intermediate positions to prevent
objectionable drafts. When direct radiators are used in conjunction with
unit ventilators, the control is usually arranged so as automatically to
open the valves to the direct radiators when the room temperature falls
about 2 deg below the setting of the thermostat for the unit ventilator.
228
CHAPTER 13 — UNIT HEATERS, VENTILATORS, AND COOLERS
Another arrangement "opens the radiator valve whenever the unit venti-
lator control reaches the full heating position. Further information on
this subject is contained in Chapter 14.
4. Distribution. This function is governed by the proper selection and
location of the unit. Diffusion and distribution are dependent upon a
relatively high velocity air stream discharged in a generally vertical
direction, and in order to insure satisfactory diffusion in the room the less
the difference between the temperature of the air discharged from the unit
and that of the room air, the better. With a final temperature above
110 F, excessive stratification of the air may be experienced. Trouble-
some drafts may be eliminated to a large extent if a static pressure is
built up in the room.
5. Recirculation of air requires less fuel than does the use of all out-
side air and aids in heating up quickly. Certain units are designed to
recirculate all air at all times, except when the admission of outside air is
needed to regulate room temperatures. Under this arrangement, the
outside air for ventilating purposes is obtained solely from infiltration, but
the amount thus obtained may or may not be sufficient to meet legal
ventilating requirements for public buildings. Recirculation of the air in
schools is therefore prohibited by ordinance in many communities.
Ventilating systems in schools should be arranged for taking in a suf-
ficient quantity of air to constitute, with infiltration, not less than 10 cfm
per occupant of a room.
6. Quiet Operation. Since the unit ventilator is generally set in close
proximity to the room occupants, it must operate with exceeding quietness.
SPLIT AND COMBINED SYSTEMS
In a split system the unit is used primarily for ventilation. Air is
delivered to the room at very near the room temperature, and enough
separate direct heaters are placed in the room to warm it to the desired
temperature, independently of the unit. Their principal advantage lies
in offsetting the cooling effect of window and wall surfaces long before
these can be heated to room temperature and in retaining heat for this
purpose after the ventilation is shut down.
Where the unit ventilator selected has a capacity more than sufficient
to warm the air needed to meet the ventilating requirements, a cor-
responding reduction may be made in the amount of direct heating surface
installed. The greater the amount of excess capacity of the unit, the more
efficient will be the temperature regulation of the room. The split
system permits the heating of the room during failure of electric current,
since the direct radiators will furnish ,,heat, but it permits a careless
operator to avoid operating the "'ventilating equipment.
A combined system employs the unit ventilator alone, its capacity being
sufficient both for ventilation and for supplying the heat loss. Direct
heating surface is omitted altogether. It becomes necessary then that the
fan be running whenever the room is to be heated but this also gives
assurance of ventilation, especially if automatic dampers are used in the
air intake from out-of-doors and in the recirculating intake arranged so as
to give a certain quantity of air from the outside (commensurate with
weather conditions) whenever the unit is operating and after the room is
229
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
heated. The cost of installation of a combined system is usually less than
that of a split system and there is less danger of overheating, but if the
electric energy fails there will be practically no heating.
LOCATION OF UNIT
The location of the unit ventilator in a room is important. Wherever
possible it should be placed against an outside wall. It is difficult to
obtain proper air distribution if the unit is erected either on an inside wall
or in a corner of the room. Standard units discharge the air stream up-
ward, but for special cases units may be installed to discharge air hori-
zontally. Units may be set away from the wall or partially recessed into
the wall to save space without materially affecting the results. The air
inlet may enter the cabinet at the back at any point from top to bottom.
VENTS
The size and location of the vent outlet is important. In many cases
the sizes for public buildings are regulated by law, but the location of the
vents generally is left to the discretion of the engineer.
Best results have been obtained with a velocity through the vent
openings nearly equal to that at which the air is introduced into the room,
thus maintaining a slight pressure in the room. Calculated velocities at
the vent openings of from 600 to 800 fpm produce the best diffusion results
from this system.
The cross-sectional area of the vent flue itself may be figured on the
basis of 15 sq in. of flue for each 100 cfm. Thus the vent flue area of a
flue for a room equipped with one 1200 cfm unit ventilating machine
would be 180 sq in. The area of vent flue opening from the room may be
figured on the basis, of 25 sq in. per 100 cfm,
In school buildings provided with wardrobes or cloakrooms the vents
may be so located that the air shall pass through these spaces, heating and
ventilating them with air which otherwise would be passed to the outside
without being used, to the best advantage. Many state codes for venti-
lation of public buildings make this arrangement mandatory.
There has been much controversy over the use of corridor ventilation
in school building practice, one group holding the view that when each
classroom has a separate vent flue there is a minimum fire risk and less
likelihood of cross-contamination, while others emphasize the economy
features of the corridor discharge and minimize the fire, contamination,
and other hazards.
CAPACITIES
Unit ventilators are available in air capacities ranging from 450 cfm to
6000 cfm and with corresponding heat capacities (above, that required for
ventilation purposes based upon an outside temperature of zero and an
inside temperature of 70 F) ranging from 30 Mbh to 144 Mbh (1 Mbh =
1000 Btu per hour). Some manufacturers furnish a unit with several
heating capacities for each air capacity, thus enabling the -engineer to
select the unit best adapted to the heating and ventilating load. Capaci-
ties should be determined in accordance with the A.S.H.V.E. Staadard
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CHAPTER 13 — UNIT HEATERS, VENTILATORS, AND COOLERS
Code for Testing and Rating Steam Unit Ventilators3. Typical capacities
are given in Table 3.
The amount of heat to be supplied by the unit ventilator will depend on
the amount of air passed through the unit and the temperature range
through which the air is heated. The weight of air (W) to be circulated
per hour is fixed by the ventilating requirements.
If no direct heating surface (radiation) is installed, the combined
heating and ventilating requirements must be taken care of by the unit
ventilators, and the total heat to be supplied is obtained by means of the
following formulae:
When all of the air handled by the unit is taken from the outside,
Ht = 0.24 W (ty - to) (1)
W = dQ (2)
H (3)
where
Q.24W
d = density of air, pounds per cubic foot.
H — heat loss of room, Btu per hour.
Hv = heat required to warm air for ventilation, Btu per hour.
Ht — total heat requirements for both heating and ventilation, Btu per hour
= H + Hv.
Q = volume of air handled by the ventilating equipment; cubic feet per hour.
t — temperature to be maintained in the room.
t0 — outside temperature.
ty = temperature of the air leaving the unit.
W — weight of air circulated, pounds per hour.
0.24 = specific heat of air at constant pressure.
From Equations 1, 2 and 3:
-fc) (4)
Example 1 . The heat loss of a certain room is 24,000 Btu per hour, and the ventilating
requirements are 1000 cfm. If the room temperature is to be 70 F and all air is taken
from the outside at zero, what will be the total heat demand on the unit if it is required
to provide for both the heating and ventilating requirements (combined system)?
Solution. H = 24,000; d = 0.075
Q = 1000 x 60 = 60,000 cfh; t « 70 F; tQ = 0 F.
Substituting in Equation 4:
Ht = 24,000 + 0.24 x 0.075 x 60,000 (70-0) = 99,600 Btu
. 24,000
0.24 x 0.075 x 60,000
70 - 92.2 F
When part of the air handled by the unit is taken from the room and the
remainder from the outside,
Ht = 0.24W0 &-*>)+ O-24 wi (h - *) (5)
•Adopted 1032. See AJ5.H.V.R. TRANSACTZO??^ Vol. 38,
2S1
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
where
= weight of air, pounds per hour taken from out-of-doors.
= weight of air, pounds per hour taken from the room.
(6)
(7)
where
Qo
a
= density of air, pounds per cubic foot at temperature to
= density of air, pounds per cubic foot at temperature t.
= volume of air taken in from the outside, cu ft per hr.
= volume of air taken in from the room, cu ft per hr.
H
+
0.24 (Wo +
H + 0.24 d0 Qo (t -
(8)
(9)
Equations 5, 6, 7, 8, and 9 may be used in the same manner as is
illustrated above for Equations 1, 2, 3, and 4. It may be noted in Equa-
tion 9, representing the total heat requirements, that as the quantity
Qo is diminished the heat requirements for the unit diminish very
materially.
In Example 1, if the quantity of air taken in from the outside is reduced
to zero, or all of the air handled by the unit is recirculated, the total heat
requirements Ht reduce from 99,600 Btu to 24,000 Btu, or to about one
fourth. Such a unit handling one-third of its air volume from the outside
and two thirds from the room would show a total heat requirement of
24,000 + 99>6Q° 7" 24'°QQ « 59,200 Btu. Units designed and operated
o
on this principle show an average heat requirement and, therefore, a boiler
capacity requirement of less than 50 per cent of that required for units
taking all their air from the outside.
If all of the air is recirculated, the total heat required is the same as the
heat loss of the room, or
0.24 W (ty - 0
TABLE 3. TYPICAL CAPACITIES OF UNIT VENTILATORS FOR
AN ENTERING AIR TEMPERATURE OF ZERO
(10)
TOTAL CAPACITY IN SQUARE FEET
CAPACIT? AVAILABLE FOR HEAT-
OF EQUIVALENT DIRECT HEATING
ING THE ROOM IN SQUARE FEET
CUBIC FEET OF
SURFACE (RADIATION)
OF EQUIVALENT DIRECT HEATING
FINAL AIR TEMPERA-
AIR PER MINUTE
SURFACE (RADIATION)
TURE (DEG FA.HR)
EDR
Mbh
EDR
Mbh
600
285
68
95
23
105
750
350
84
115
28
105
1000
455
110
150
36
105
1200
565
136
190
46
105
1500
705
169
235
56
105
232
CHAPTER 13 — UNIT HEATERS, VENTILATORS, AND COOLERS
If the heat loss of the room is to be taken care of by the direct heating
surface, the unit ventilators will be required to warm the air introduced
for the ventilating requirements. Therefore:
Hv = 0.24 W (ty - t0) (11)
In this case t? should be equal to or slightly higher than i. If the unit
ventilator were of such capacity as to exactly provide for the ventilating
requirements, the direct radiation would be selected on the usual basis.
However, it is necessary to employ a unit which may not exactly meet the
ventilating requirements, since standard units are usually rated in terms
of the volume of air that will be delivered at a certain temperature ty for
an initial temperature of tQ. Therefore a certain amount of heat (flh)
may be available from the unit ventilator for heating purposes, as pre-
viously stated, and the amount of equivalent direct heating surface may,
if desired, be deducted from the amount required for heating the room.
ATTIC FANS
Attic fans, used during the warm months of the year to draw large
volumes of outside air through a house, offer a means of using the com-
parative coolness of outside evening and night air to bring down the
inside temperature of a house.
Because the low static pressures involved are usually less than Y% in. of
water, disc or propeller fans are generally used instead of the blower or
housed types. The fans should have quiet operating characteristics, and
they should be capable of giving about thirty air changes per hour. The
two general types of attic fan installations in common use are:
Open attic fans, in which the fan is installed in a gable or dormer and
one or more grilles are provided in the ceilings of the rooms below.
Fresh air, which enters the house through open windows, is drawn into
the attic through the grilles, and is discharged out-of-doors by the fan.
An attic stairway may be used in place of the central grille. It is
essential that the roof and the attic walls be free from air leaks.
Boxed-infan, in which the fan is installed within the attic in a box or
housing directly over a central ceiling grille, or in a bulkhead enclosing
an attic stair. The fan may be connected by a duct system to the
grilles in individual rooms. Fresh air entering through the windows of
the rooms below is discharged into the attic space and escapes to the
outside through louvers, dormer windows, or screened openings under
the eaves.
The locations of the fan, the outlet openings, and the grilles should be
chosen after consideration of the room and attic arrangement in order to
give uniform air distribution in the individual rooms served. If the outlet
for the air is not on the side away from the direction of the prevailing
wind, openings should be provided on all sides. Kitchens should be
separately ventilated because of the fire hazard, and to prevent the
spread of cooking odors.
The operating routine which will secure best results with an attic fan is
an important consideration. A typical routine might require that in the
late afternoon when the outdoor temperature begins to fall, the windows
233
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
on the first floor and the grilles in the ceiling or the attic floor should be
opened, and the second story windows should be kept closed. This will
place the principal cooling effect in the living rooms. Shortly before
bedtime, the first floor windows may be closed and those on the second
floor opened, to transfer the cooling effect to the sleeping rooms. A time
clock may shut off the fan before waking time, or the fan may be stopped
manually at a later hour.
A disadvantage arising from the passing of a great amount of outside
air through a house is the dust nuisance, which varies considerably in
different locations. Persons suffering from allergic diseases caused by air-
borne pollens will have their troubles increased with attic type coolers.
Some typical data on an attic fan installation in an average six-room
house of frame construction containing 14,000 cu ft and located in the
southern part of this country are :
Installation cost..
Fan data
Operating period..
Power consumption
$75 to $400, average $250
9000 cfm average, 280 rpm if belt driven, 570 rpm if direct
connected, 500 watts input
April 15 to October 15, intermittently as weather con-
ditions demand
500 kwh per year for 8 months' operation
UNIT COOLERS
A unit cooler, as defined in Chapter 41, is a device usually comprising
an extended-surface element and a motor-driven fan mounted integrally
in a housing, suitable to be placed within or adjacent to the room served.
The refrigerating medium is brought to the unit from an outside source,
and the fan drives air over the cooling element; generally, no d,ucts are
attached to inlet or outlet. With provision for filtering the air and taking
in outdoor air for ventilation, the apparatus becomes a unit conditioner
(Chapter 12). An alternative design uses chilled water or brine spray for
cooling the air; it is essentially a small compact air washer with built-in
fan and accessory equipment.
The principal field for unit coolers is in cold-storage plants, fur-storage
vaults, packing houses, provision stores, brewery fermentation and stock
rooms, and industrial process work. Coolers have, to a considerable
extent, supplanted the bunker coils heretofore placed on ceilings and walls,
because of demonstrated advantages with respect to : compactness, first
cost, maintenance expense, damage from drips, ease of defrosting, main-
tenance of sanitary conditions, uniformity of temperature throughout the
space served, and uniformity of temperature under variable load con-
ditions, as well as control of humidity and circulation of room air when
conducive to improved results.
A typical suspended unit is shown in Figs. 3 and 4. A motor-driven
propeller-type fan is bracketed to the frame of a sheet-metal housing that
contains an extended-surface coil, and a double set of louvers acting also
as a moisture eliminator is provided at the outlet side. The horizontal
louvers are adjustable to direct the air downward, horizontally, or upward,
as desired. The lower part of the housing forms a drip pan, requiring a
drain connection to dispose of the condensation when dehumidifying air
234
CHAPTER 13 — UNIT HEATERS, VENTILATORS, AND COOLERS
at usual room temperatures, or of the water when defrosting in low-
temperature service. A cabinet-type unit for floor mounting is shown in
Fig. 5 ; other designs are illustrated in the Catalog Data Section at the rear
of this volume.
« ^ — i
PI— Hon^r
I I „ Water I
Connection
Louvres
Connection
FIG. 3. CEILING UNIT
l/ertfca/ Diffusing
Eliminators
Front
On L
% Orif>
Conn
FIG. 4. ELEVATION THROUGH LINE AA
Depending upon the arrangement of the cooling coil, chilled water,
brine, or a direct-expansion refrigerant may be employed. For cooling
service at or near ordinary room temperatures, the considerations
affecting a choice of cooling medium are those discussed in Chapter 12 for
unit air conditioners. At lower temperatures, as for cold-storage, the
235
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
refrigerant system is usually dictated by the requirements of other
refrigeration services supplied from the same condensing unit or from a
central plant.
Details of construction employed in unit coolers are generally similar to
those for unit air conditioners, with special attention paid to the use of
non-corroding materials. Temperature control is obtained by starting
and stopping the fan, with or without regulation of the cooling liquid or
direct-expansion refrigerant admitted to the coil. Usually, a thermostatic
control is provided ahead of the expansion valve at the inlet to the coil,
tending to maintain constant temperature and pressure inside the coil
regardless of cooling load, with a float at the outlet to prevent accumu-
lation of liquid refrigerant in amounts sufficient to interfere with dis-
1 til
1
fr"^"f.
^•••T""K
~Tr'"2~Kt"
~jH~ if"
1 1 I
7 I i u
(1
i<
J , Coo///7y
H « £— = -- = --
£"/e/77en?-p> |
!
!' ii e--=.-=- =
ii *_,j
!' ' i
aai""V*
II j 1
i i^ ;i
J
ii ! / r/oor-i?
rtp Pon ^ ,
/v//
V V //////////////
s/s//////// ////?///
///
FIG. 5. CABINET TYPE COOLING UNIT
tribution between the various unit coolers served by a central condensing
unit.
Ratings of unit coolers may be expressed in Btu per hour or in tons of
refrigeration, with specified quantity, temperature, and humidity of air
at the inlet, and with a stipulated pressure or temperature maintained
within the cooling coil when using direct-expansion refrigerants. When
chilled water or brine are used as the cooling media, the quantity and
inlet temperature must be given. Ratings and dimensions of representa-
tive makes of unit coolers are given in the Catalog Data Section.
PROBLEMS IX PRACTICE
1 • Is it better to use high pressure or low pressure steam in unit heaters?
The answer to this question depends upon the following circumstances: If steam is used
only for heating purposes, it is usually best to design the entire system for low pressure
steam. When steam is generated at high pressure for other purposes, it can be used
either at full boiler pressure or at reduced pressure in the unit heaters. If the steam
pressure is reduced, the heating elements should be capable of withstanding the full boiler
pressure. When steam at full boiler pressure is used in the heating elements, the heating
surface should be reduced so that the outlet temperature will not be more than 70 F
higher than the inlet temperature. Wjth the use of high pressure steam special care must
be exercised in venting the units of air, in preventing flash steam in the returns, and in
preventing corrosion from superheated returns.
236
CHAPTER 13 — UNIT HEATERS, VENTILATORS, AND COOLERS
2 • How should heat losses he calculated for a huilding using unit heaters?
The heat losses should be calculated in exactly the same manner as for any other heating
system. If the method of calculation takes into consideration the variation in tem-
perature from the floor to the ceiling, the temperature variation should be reduced when
calculating the heat losses for a unit heater job. This is advisable because with unit
heaters the temperature variation between the floor and the ceiling is from }•£ to 1 F
per foot of elevation, whereas with direct radiators or pipe coils, this variation may be
twice as great. Unless the ceiling height is more than 15 ft, the temperature variation
between the floor and the ceiling is usually neglected when unit heaters are used.
3 • On what hasis should unit heaters he selected?
Unit heaters should be selected to furnish enough heat to offset the heat losses and to
circulate the air in the room fast enough to provide good heat distribution. In the
average building, if the outlet temperature does not exceed the inlet temperature by more
than 70 F, sufficient air capacity will usually be provided for proper circulation if the
units are selected strictly on the basis of heating capacity. However, if the units are
hung unusually high or if the heat loss is low in proportion to the volume of the room,
then, in order to obtain the desired air capacity, it is usually necessary to employ more
heaters than are required to offset the normal heat loss. Inasmuch as the heat distri-
bution depends upon the outlet temperature, the outlet velocity, the character of air flow
from the heater, the height at which the heaters are hung, and the size of the heater
itself, the manufacturers' literature should be carefully studied in determining the exact
number of heaters to be employed.
4 • Is it satisfactory to use superheated steam in unit heaters?
Superheated steam can be satisfactorily used in unit heaters provided the capacity is
based on the saturated steam temperature and not on the total temperature. If un-
usually high superheat is used, trouble may be experienced from the excessive expansion
and contraction of the heating elements.
5 • Is it satisfactory to install one unit heater as the total load on a coal
fired hoiler?
Such an arrangement is impractical if the unit heater is started and stopped in keeping
with the room temperature. However, if the room temperature controls the steam pres-
sure and the unit heater is arranged to start when there is steam in the mains and to
stop when there is no steam in the mains, such an installation will be satisfactory.
6 • Will a unit heater with a slow speed fan he more quiet than one with a
high speed fan?
The speed of the fan is no indication of quietness. Quietness is a function of the type,
diameter, blade form, speed, and location of the fan.
7 • Is it satisfactory to use steam at pressures less than atmospheric for unit
heaters?
If the air inlet temperature is above freezing, steam at any pressure may be used in the
unit heater. If the inlet temperature is below freezing, steam of at least 5 Ib pressure
(or with a positive 5 Ib pressure differential between supply and return) should be used,
and the steam supply should never be throttled or the heating element may be frozen.
8 • In general, what is the primary function of a unit ventilator?
To maintain the desired room air conditions as to temperature, air change, and air
cleanliness, without drafts regardless of variations in outdoor temperature, occupancy,
sun heat, and wind.
9 • What are the usual working parts of a unit ventilator?
A fan and motor assembly, a set of heating elements, outdoor and indoor air dampers.
filters, outlet grille, some method of controlling the outlet temperature above a minimum
of 60 F, and some method of varying the outlet temperature in keeping with the room
requirements. All of these parts are usually enclosed in an attractive steel cabinet in
which the piping is concealed.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
10 • Do all unit ventilators introduce a constant amount of outdoor air?
Certain types employ full recirculation except when outdoor air is obtained by throttling
the steam valve on the heating element so the proportion of outdoor air to room air is
varied. This is a very economical type of unit ventilator but in some communities it
cannot be used because of existing laws which require that some fixed amount of outdoor
air be introduced whenever the room is occupied. Certain types of units are designed to
always take in a minimum quantity of air from the outside and to automatically vary
this with the weather.
11 • Where should a unit ventilator he located?
In the center of the longest outside wall under the windows.
12 • What further precaution should he taken in locating unit ventilators?
With most unit ventilators, a high velocity jet of air is discharged toward the ceiling at a
slight pitch toward the room ; all unit ventilators should be installed in such manner that
this jet is not interfered with. For this reason the air should be distributed on a flat
ceiling without beams, but if beams are present, the unit ventilator should be so located
that the air will be discharged parallel to the beams.
13 • When unit ventilators are installed to employ variable recirculation, what
special precautions are necessary?
Where partial recirculation is employed, some effective means should be installed within
the cabinet of the unit ventilator to prevent unheated outdoor air from being blown into
the room through the room air opening while the unit is mixing indoor and outdoor air.
This means may be self-operating dampers placed in the path of ^the room air, or filters
so arranged that the outdoor air must pass through them before it can enter the room.
14 • Generally speaking, should direct radiators be used in addition to unit
ventilators in school classrooms?
The best practice in schoolrooms is to place as much heating capacity as possible in the
unit ventilator itself. However, in selecting the unit ventilator, the outlet temperature
should not exceed 110 F and the rate of air circulation should not exceed 9 room volumes
per hour (anemometer measurement) or 7^4 room volumes per hour (A.S.H.V.E. Code
measurement). If the heating capacity under these conditions is sufficient to heat the
room, no additional radiation is required. If the heating capacity is not sufficient, direct
radiation should be used to make up the required total. Radiators always tend to offset
the chilling effect of cold walls and windows quicker than warm air does.
15 • Are vent outlets required with unit ventilators?
Though experience has indicated that in practically all school and office buildings the
cracks around the windows, doors, and baseboards are so numerous that vents are not
required, in many communities vents are required by existing laws. In some cases the
sizes are also stipulated in the laws. When the size is not stipulated, vents should be
designed on the basis of a velocity not greater than 600 ft per minute. Vent flues should
always be provided with a damper in order that they may be throttled.
238
Chapter 14
AUTOMATIC CONTROL
Apparatus Sensitive to Temperature, Apparatus Sensitive to
Relative Humidity, Apparatus Sensitive to Pressure, Accessory-
Apparatus, Temperature Control Systems, Control of Automatic
Fuel Appliances, Individual Room Control, Zone Control, In-
dustrial Processes, Air Conditioning Systems, Seasonal Operation
\ UTOMATIC controls can be installed on any type of heating,
J~\. ventilating, or air conditioning system to maintain desired con-
ditions automatically, and with maximum operating economy. The
variety of automatic control equipment available is such that a suitable
control system can be devised without difficulty, provided that the con-
ditions to be maintained are known and the control equipment is properly
chosen. This chapter outlines briefly the various types of control appar-
atus and indicates the method of* their application to typical heating,
ventilating, and air conditioning systems. Specific control devices and
systems are described in the Catalog Data Section of THE GUIDE.
Controls are applied for the following reasons:
1. To maintain conditions required for human comfort and efficiency.
2. To maintain conditions required for industrial processes.
3. To obtain economy in operation.
4. To provide necessary safety measures.
CONTROL APPARATUS
The various pieces of control apparatus may be grouped under the
following general headings:
Apparatus Sensitive to Temperature
Temperature-sensitive devices which will respond to changes in tem-
perature, and which will motivate equipment to compensate for the
changes, are usually called thermostats. They have many specialized
forms for use in specific control applications. Thermostats are the
detectors of a control system which identify changes in desired tempera-
ture conditions and automatically call for compensating action.
Thermostats are actuated by various means, all of which have the
common characteristic of responsiveness to small changes of temperature.
The actuating element may be a piece of bi-metal in straight, helical, or
spiral form (Fig. 1), which, by bending slightly as the temperature
changes, actuates an electric or pneumatic switch to govern the controlled
apparatus; or the actuator may be a diaphragm, bellows, or tube filled
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
with a volatile liquid (Fig. 2) in such way that expansion and contraction
with changes in temperature will operate the controlled apparatus by a
direct mechanical, electric, or pneumatic connection.
A room or watt thermostat in its simplest form contains a single tempera-
ture-sensitive element which is so set that it maintains, by actuating the
controlled system, a single temperature. The two-temperature or dual
thermostat has two temperature-sensitive elements, one of which is set for
a higher temperature than the other. Such a thermostat is used on day-
night systems where the night temperature is to be lower than that
STBAIGHT 3TK/P
b. Spiral Type
a. Straight Strip Type
c. Curved Strip Type
FIG. 1. TYPICAL BI-METALLIC THERMOSTATIC ELEMENTS
Volatile Liquid
FIG. 2. DIAPHRAGM TYPE THERMOSTAT
maintained during the daytime hours. Switching the control from one
element to the other is accomplished by an external or an internal switch,
which can be operated manually or by a time device.
Duct type thermostats are used in systems where the equipment must
respond to changes in the temperature of the air passing through a duct.
In their usual form, these thermostats are so constructed that their
switching mechanism is outside the duct, while the temperature-sensitive
element projects inside into the air stream.
Thermostats which operate in liquids have the same general construc-
tion as duct thermostats except that the sensitive element is usually
enclosed in a tube to keep it from direct contact with the liquid. They
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CHAPTER 14 — AUTOMATIC CONTROL
are used in pipes, vats, and tanks, and are called immersion thermostats.
Such a thermostat is Illustrated in Fig. 3.
Sometimes surface thermostats are used in place of duct or immersion
thermostats. These devices, so constructed as to respond to changes in
temperature of the surface of the duct or vessel containing a fluid, are
clamped or screwed to such surfaces in a manner which will provide as
rapid as possible heat transfer between the surface and the sensitive
element.
Apparatus Sensitive to Relative Humidity
Devices which are responsive to changes in the relative humidity of the
surrounding air, and which will motivate equipment to compensate for
the changes, are called humidistats or hygrostats. These may vary con-
siderably in their sensitive elements, but they all operate through con-
necting equipment which automatically causes humidifying apparatus to
supply more or less moisture as required. Some of the more complicated
VACUUM
RELEASE AT AWCUUtt
GREATER THAU THAT
CAUSED BY! JW POOP
THERTIOSTATIC TRAP
-RETURN TO
VACUUM PUMP
Fic. 3. SELF-CONTAINED THERMOSTAT ON HOT WATER TANK WITH VACUUM RETURN
ones contain essentially two thermostats, one working on a dry-bulb
temperature and the other on a wet-bulb temperature ; by proper inter-
connection of the parts they operate to maintain a definite relation be-
tween these two temperatures. Other devices use elements, directly
sensitive to humidity, made of special wooden blocks, human hair, fiber,
membranes, or strips of prepared paper. Hygrostats are available for
use with both electric and pneumatic control systems.
Apparatus Sensitive to Pressure
Use is made of devices which are responsive to changes in pressure, and
which will motivate equipment to compensate for the changes. Such
devices usually depend upon the flexing of a diaphragm or bellows as
caused by varying pressures or vacuums to obtain the mechanical move-
ment necessary to actuate an electrical or pneumatic switch.
Apparatus Which Operates Valves
Apparatus which is so mechanically or electrically equipped that it will
open and close valves, and possibly give them fixed intermediate positions
in any pipe line of a heating, ventilating, or air conditioning system, is
termed a valve operator. The function of a valve operator is, essentially,
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
to move the plunger of a valve in a manner required by its type and
construction. For instance, in a single-seat valve, the disc is moved
against the seat and held there with sufficient pressure to prevent flow.
A three-way valve, however, requires a valve operator that will place the
double disc, as required, between the two seats. Each type of valve has
special characteristics to which a valve operator must be adapted.
When a valve is used in shut-off service the valve operator simply
opens the valve or closes it completely, as required. When the valve is to
provide throttling service, a different type of valve operator is used so
that the valve may be held at any intermediate position between open
and closed. Valve operators use as their power source either compressed
air (pneumatic system), electricity (motor-driven type of solenoid type),
or a volatile liquid (direct-connected type).
Apparatus Which Operates Dampers
Apparatus which is so mechanically or electrically equipped as to open
and close dampers, and possibly give them fixed positions, in accordance
with the purposes of the system using the dampers is termed a damper
operator. Damper operators are made for opening, closing, and position-
ing the dampers in the ducts of heating, ventilating, or air conditioning
systems in the same way that valve operators regulate the valves. They
receive their signals from thermostatic or manual switches.
The sources of power used are compressed air, electricity, or volatile
liquids. The damper operator is connected to its damper by direct con-
nection or by a linkage, according to conditions, and it can usually be
mounted either outside or inside the duct in which the damper is located.
Accessory Apparatus
Accessory apparatus is that additional equipment at the terminals of a
control system necessary to make it operative. Every temperature con-
trol system requires a number of accessories, which will vary with the
different types of systems. For instance, pneumatic systems require a
compressor and a storage tank for the air which operates the units, and
low- voltage electric systems require a .transformer or generator to provide
the required current.
Most of the larger control systems will have some sort of central switch-
board which may include indicating and recording devices as well as
control switches. Thermostat guards are generally used In gymnasiums,
schools, and places of assemblage for protective purposes. Time switches
and similar devices are often important parts of certain types of control
systems. Couplings, mountings, and indicators are often parts of a
system.
Connecting Apparatus
Connecting apparatus is that equipment used to connect the various
parts of a control system. Because the parts of the system are often some
distance apart, the connecting means are important, and the connections
must be properly planned and made.
The connecting elements are fairly obvious. The pneumatic system
uses compressed air carried in small pipes and tubing. Electric systems
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CHAPTER 14 — AUTOMATIC CONTROL
are wired for low-voltage or high-voltage power supply. Systems em-
ploying volatile liquids generally use flexible tubing if there is distance
between the sensitive ,bulb and the operating unit. Each form has certain
limitations which the designer of the system must consider.
Since few control installations are alike, the manufacturers of control
apparatus usually maintain engineering departments staffed by experi-
enced men whose advice may be had on control problems. Progress in
automatic control has been rapid in the past few years and the field of
automatic control has become specialized.
TEMPERATURE CONTROL SYSTEMS
The control of direct radiation is simple. Each radiator has a valve on
its steam or water supply, with a thermostat to govern the opening and
closing of the valve to maintain the desired uniform temperature. One
thermostat may control the valves on all the radiators in a room, or, if the
room is large, more than one thermostat may be used, with each one
governing one radiator or a group of them. Unit type thermostatic
valves may be used, one on each radiator.
The location of wall thermostats is important. They must be on inside
walls where they will not be affected by drafts of either warm or cold air,
but where they will be exposed to general room conditions. If vibration
is present, they must be mounted on shock-absorbing bases. If the walls
are abnormally hot or cold, the thermostats must be mounted on heat-
insulating bases. The connecting means can be concealed in the wall,
under the floor or ceiling, or behind baseboards or moldings.
Modulating type valves cannot be used successfully on one-pipe steam
systems because the partial opening of valves will not allow the con-
densate to escape against the incoming steam.
A discussion of steam heating systems is given in Chapter 31, and
further information on control requirements of direct radiation may be
obtained therefrom.
Control of Unit Heaters
Unit heaters are commonly ceiling-hung or floor-mounted units con-
sisting of a steam or hot water coil with a fan behind it to force air past
the coil and into the room. Vanes direct the warm air flow. The simplest
and commonest way to control a unit heater is to have in the heated space
a thermostat which will turn on the fan when heat is required and shut it
off when the demand is satisfied. However, where there is natural
circulation through the unit, it is advisable to put a valve on the steam or
hot water supply line and arrange it so the steam will be turned on only
when the fan is running,
As a precaution against allowing the unit heater motors to continue to
run if the steam supply fails or is for some reason shut off, either a pres-
surestat or a thermostat in the supply line, or a thermostat on the return
line may be installed to stop the motor when the pressure or temperature
in the supply line, or the temperature in the return line, drops below a
predetermined point. When the fan and the steam are controlled simul-
taneously, such thermostat will also prevent the blowing of cold drafts.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
The net result in any case will be that the fan will run only when there
is heat in the coil.
Control of Unit Ventilators
The unit ventilator presents a different control problem than the unit
heater. Generally this type of unit draws its supply of air from the out-
side, heats it, and introduces this air into the room under control. There
are many types of unit ventilators on the market. Some have a mixing
damper by which the temperature of the air entering the room may be
varied, others have valves for this purpose, and still others use a com-
bination of the two. Regardless of the construction of the machine, the
essential requirement is that the temperature of the air delivered to the
room should change slowly and remain as near room temperature as
possible. Frequently direct radiators are used in conjunction with the
unit ventilators to supply additional heat in extremely cold weather or
for quickly heating up the room.
The four general types of control for unit ventilators are as follows :
1. A damper operator, which is controlled by a room thermostat, is attached to the
mixing damper. When the thermostat calls for heat, the damper is moved to a position
which forces more air through the heating unit and thus increases the amount of heat
supplied to the room. This action must be gradual so that the air temperature may be
changed slowly to prevent the drafty condition caused by supplying first hot and then
cold air. This simplest arrangement is often condemned because it frequently results
in drafts.
2. In mild weather the heating unit frequently supplies sufficient heat to cause over-
heating of the room, even though all of the air is by-passed around the heating unit. To
avoid this fault a valve is placed on the heating unit to close the steam supply when the
damper is by-passing all of the air. This valve is used in addition to the damper operator
explained in the foregoing paragraph, but though giving better results, it may fail to
prevent drafts.
3. In some unit ventilators one or more heating units are used without a mixing
damper. A gradual-acting valve on each heating unit controls the supply of steam to the
unit to give the proper amount of heat required to maintain the desired room tempera-
ture. A thermostat to govern each valve may be installed in the room, or one^thermostat
may be used for all valves, but unless a thermostat is placed directly in the air stream of
each unit, drafts may be encountered.
4. Another type of unit ventilator is arranged so that all recirculated air passes
through the heating unit, and the outside air is introduced into the room for cooling
purposes only. The outside air damper and the recirculated air damper are interlocked
so that one damper operator will control them. In addition a valve operator is placed
on the heating unit. Both of the operators should move gradually to avoid drafty con-
ditions. When the thermostat calls for heat, the damper operator slowly closes the
outside air damper and simultaneously opens the recirculating damper; if this does not
meet the demand, the valve on the heating unit opens until the room temperature reaches
the desired point.
For additional information on the control of unit ventilators, refer to
Chapter 13.
Central Fan Heating and Ventilating Systems
The numerous types of central fan systems present many control
problems. In general they all have one point in common, namely, that
the temperature change may be very fast because of rapid circulation.
System for Ventilating Only (Split System). Fig. 4 shows an accepted
control for ventilating systems. Thermostat A located in the outside air
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CHAPTER 14 — AUTOMATIC CONTROL
duct is set just above freezing, and controls a valve C on the first heating
coil. This valve is either completely open or completely closed. The by-
pass damper B and the other two valves D and E are controlled by a duct
thermostat F located in the discharge duct from the fan. If the tempera-
ture of the air surrounding the thermostat F increases, the damper is
moved automatically to admit more cold air. Should this not reduce the
temperature sufficiently, the valves on the heating coil will be closed
gradually and in sequence until the correct temperature is reached. The
opening or closing of the damper B and the valves D and E must be
gradual or there will be a wide fluctuation in air temperature.
In ventilating systems it is customary to supply air to the ventilated
spaces at an inlet temperature approximately equal to the temperature
maintained in the rooms. The radiators therefore are designed to take
care of all the heat losses from the room. Hence, in order to maintain
Electric or pneumatic
power source
FIG. 4. CONTROL OF A SPLIT SYSTEM OF VENTILATION
controlled room temperatures it is necessary to use room thermostats
governing control valves placed on the radiators. With this type of
central fan system it is possible to ventilate a large number of rooms by
means of one fan.
In some installations, such as in theaters or auditoriums, it is difficult
to install sufficient direct heating surface to offset the heat losses from
the room. Also there are installations where a short heating-up period is
allowed before occupancy of the room, and it is advisable to use the
entire heating capacity of the ventilating system for this purpose.
In central fan systems, air washers are often used and in such cases, due
to the effect of temperatures on humidity, additional control is required.
Fig. 5 shows such an arrangement with control of the second tempering
heating unit by the air washer temperature and with the usual control
of the first tempering heating unit by the outside temperature. This
permits the air to be kept cool while passing through the washer so that
too much moisture will not be absorbed. Fig. 5 also shows control of the
reheating units by a duct thermostat in the fan discharge, and the
application of a pilot thermostat to a system of this sort.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Combined Systems. There are various central fan systems which are
used for both heating and ventilating. They are usually arranged with
tempering heating units, automatically controlled to provide a minimum
temperature for ventilating only, and additional heating units to supply
the heating requirements. Fig. 6 shows a type of system which has the
reheating units located in the fan room. Tempered air at about 70 F is
supplied to the fan. It may be further heated by the reheating units, or it
may pass into the tempered air chamber. A room thermostat controls a
gradual-acting damper operator on the double mixing damper in the warm
and tempered air chambers. When the thermostat calls for heat, the
Electric or pneumatic
power source /
Multiple point
insertion thermostat
FIG. 5. USE OF PILOT THERMOSTAT ON VENTILATING SYSTEM WITH AIR WASHER
damper operator moves the dampers so that more air is taken from the
warm air chamber. It is essential that the double mixing damper be
moved slowly to prevent alternate blasts of hot and cold air from being
supplied to the room.
Outside Air, Recirculating, and Vent Dampers. In all types of plenum
systems, the outside air damper is usually opened and closed by a damper
operator. This operator may be controlled from a switch in the engi-
neer's room or it may be operated by a relay in the fan motor circuit.
When the ventilating fan is started, the relay causes the damper operator
to open the outside air damper. '
Recirculating dampers and vent dampers may also be opened and
closed by means of damper operators controlled from remote locations.
Generally these damper operators are positive acting and are either
completely opened or closed. However, in some cases where part out-
side air and part recirculated air is used, it is advantageous to use damper
operators which have a certain number of definite positions. With this
type of operator it would be possible to use 75 per cent outside air and
25 per cent recirculated air, or any other proportions which might be
predetermined. These damper operators are controlled from switches
generally mechanically interlocked so that the total opening of the two
dampers is 100 per cent.
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CHAPTER 14 — AUTOMATIC CONTROL
Hand- Fired Coal Systems
In small buildings the heating plant may be controlled by a single
thermostat located in a key room in the building, instead of each room
having its own control.
The most common control for a hand-fired furnace or boiler consists of
a room thermostat and a furnace regulator of some type. The thermostat
should be located in a representative room; never, of course, near the
chimney or heat flue, too close to a radiator, or in a drafty hallway, and
preferably on an inside wall. The regulator is attached to the draft and
check dampers of the furnace. When the temperature of the air sur-
FIG. 6. CONTROL OF MIXING DAMPERS WITH INTERMEDIATE-ACTING THERMOSTAT
rounding the thermostat drops, the thermostat causes the furnace regu-
lator to open the draft and close the check damper. As soon as the room
comes up to temperature, the draft is closed and the check damper
opened. With this arrangement on hot water heating systems it is
advisable to install an immersion thermostat in the boiler. This thermo-
stat should be connected with the room thermostat so that both must call
for heat before the draft is opened, but either one may cause the draft to
be closed. On- warm air systems it is advisable to use a bonnet thermostat
and on steam heating systems a pressure limiting device, in series in each
case with the room thermostat. If the temperature of the heating
medium becomes too high, the drafts will be closed even though the room
thermostat continues to call for heat*
There have been some recent improvements in controls of this type,
involving the use of special types of thermostats and auxiliary apparatus
which will give closer control and prevent overheating in mild weather.
CONTROL OF AUTOMATIC FUEL APPLIANCES
It is essential that automatic temperature control be used with oil
burners, gas burners, and stokers to aid economical operation. There are
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
many types of burners and many types of control, but there are some
points common to all. First, a room thermostat is located in a key
position in the building to maintain a given temperature at that point.
Safety devices are installed in connection with this thermostat so that a
failure of the ignition, power, or fuel supply will shut the system down.
The same limit controls as recommended for coal burning should be
used.
Oil Burners
Fig. 7 illustrates diagrammatically the essentials of an oil burner con-
trol circuit. Three thermostats are employed as shown in the illustration.
Thermostat No. 1 will stop the burner when the room temperature is too
high and No. 2 will stop the burner when the temperature of the heating
medium exceeds the setting of thermostat No. 2. Both temperatures
must be below their respective thermostat settings to start the burner.
Thermostat No. 3 responds to the flame temperatures and in conjunction
with the control switch acts as a safety to stop the burner if the latter
fails to ignite or burn properly as demanded by thermostats No. 1 and 2.
Domestic Applications
Steam and hot water heating plants are often used to provide heat for
the domestic hot water supply as well as for heating the building. Fig 8
illustrates one such system. The burner control is similar to that shown
in Fig. 7 except that either the room thermostat or the tank thermostat
may start the burner. If the house is warm enough, the house tempera-
ture control valve will remain closed, and the boiler, through the coil
heater, will warm the water in the storage tank when the tank thermostat
starts the burner. The burner will stop only when both thermostats are
satisfied, or when the steam pressure shall have reached that allowed by
the pressurestat. Much the same control is applied to gas burners and
automatic coal stokers.
Gas Heating Appliances
On account of the ease and effectiveness with which the fuel can be
controlled, gas-burning appliances are particularly adaptable to full
automatic control. Standard equipment on a steam boiler generally in-
cludes provision for control through a room temperature thermostat, a
steam pressure regulator, and a device which shuts off the gas in the event
that the water level becomes too low. Practically all gas boilers are or
may be equipped with automatic safety pilots which shut off the gas if the
pilot flame is too low.
Water boilers are adapted to operation under thermostatic room tem-
perature control and are also provided with water temperature control
equipment. Warm air furnaces can be under the control of thermostats
in the spaces being heated, as well as thermostats located in the heat ducts
for the purpose of preventing unpleasantly hot air reaching the heated
spaces. Variations in the pressure under which the gas is supplied to the
appliance are controlled by means of a gas-pressure regulator. This is an
essential part of practically all makes of gas-burning heating appliances ;
in fact, a gas-pressure regulator is required by the American Gas Associa-
tion on all approved gas boilers, warm air furnaces (except floor furnaces) ,
and unit heaters.
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CHAPTER 14 — AUTOMATIC CONTROL
INDIVIDUAL ROOM CONTROL
The most elaborate type of automatic control is that by which the
temperature in each room or in a group of rooms can be controlled. A
thermostat in each room governs the valves on the radiators in that room,
FIG. 7. ELECTRIC THERMOSTAT APPLIED TO OIL-FIRED HEATING SYSTEM
Room
Thermostat
To Hot Water
lank
^Thermostat Pressure-^
, <5tat \
House Temperature
"Control Vafve
^ To Radiation
-Mbfart '=^,rrom Radiation
L/rre
^AutofT7at/c Fuel Burner
FIG. 8. TYPICAL ARRANGEMENT OF STEAM OR VAPOR SYSTEM WITH Two
THERMOSTATS CONTROLLING AUTOMATIC FUEL BURNER USED
FOR HOUSE HEATING AND WATER HEATING
opening them as heat is called for and shutting them when the room is
warm enough. The thermostats are all connected in relay so when any
thermostat is calling for heat, an automatic burner will supply steam, hot
water, or warm air, to the system ; and when all the thermostats are satis-
fied, the burner will shut off. This is an excellent arrangement for larger
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
residences, and it may be applied, in modified form, in houses which have
one room or a section that is difficult to heat.
ZONE CONTROL
Zone control is a step between a single thermostat and individual room
temperature control. The building is first divided into sections or zones
which may have quite different heat requirements. With this method of
control :
First: The zoning should be done with reference to the compass, since
the north and west quarters in most localities require considerably
more heat during the heating season than do the south and east
quarters.
Second: Most large office buildings have more or less space occupied
by merchants, and some by clubs, or restaurants, which have short
hours of occupancy. Much can be accomplished in zoning with
reference to the kind of occupancy of space. For additional infor-
mation on this subject, refer to Chapter 31.
Variations of the usual zone control methods by the use of recently
developed special devices have been quite successful in obtaining greater
economy from heating systems. Frequently these use an outside ther-
mostat or group of thermostats which adjust the operation of the controls
to conform to variations in weather conditions.
COOLING UNITS
Cooling units are readily adaptable to thermostatic control. Several
arrangements are as follows:
1. Room thermostat in conjunction with a magnetic or motor-operated valve to
regulate the flow of refrigerant to coil. Usually the fans operate continuously.
2. Room thermostat to control the operation of the compressor. The fans operate
continuously.
3. Room thermostat to control the operation of the fan motors.
4. Room thermostat to control the operation of the fan motor and the compressor
motor simultaneously.
5. Room thermostat to control the operation of the compressor with back pressure
control to regulate the fans.
INDUSTRIAL PROCESSES
There are many industrial processes requiring automatic temperature
and humidity regulation. The control equipment operates on the same
principles that have been described, but it is often especially designed for
each particular process. Each installation, or the installation for each
process, is likely to be a problem peculiar to that process.
AIR CONDITIONING SYSTEMS
The following fundamental principles should be borne in mind in the
solution of problems involving the control of air conditioning systems:
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CHAPTER 14 — AUTOMATIC CONTROL
1. Dew-point temperatures vary only with the amount of moisture. That is, no
matter how much a given mixture of air and water vapor is heated or cooled, the dew-
point temperature remains the same, as long as there is no addition or subtraction of
water. Cooling below the dew-point temperature will, of course, cause condensation of
the water vapor. Also, at the same temperature, there is always the same proportion of
water vapor in the saturated mixture, provided sufficient water and time are furnished
for saturation.
Table 5, Chapter 1. shows the amount of moisture required to saturate a space at
various temperatures. When the proper amount of moisture is determined, it is only
necessary to set the air washer (dew-point) thermostat for the corresponding temperature
of saturation; then if the air Centering the washer has more humidity than desired, the
excess will be condensed ; and if it has less, the deficiency will be absorbed from the sprays.
For example, the dew-point temperature at 70 F and 40 per cent relative humidity is
45 F. Therefore, if the air temperature is maintained at 45 F as it leaves an air washer
(assuming it is fully saturated) and then is heated to 70 F, it will have a relative humidity
of 40 per cent. If it is desired to maintain these conditions in a given space, the air tem-
perature can be raised to any necessary point, say 120 F (at which the relative humidity
will be only 9 per cent) . When the heat in the air has been dissipated, the space tem-
perature being maintained at 70 F, the relative humidity will be 40 per cent.
2. Within ordinary operating ranges, saturated air will have a relative humidity of
approximately 50 per cent when its temperature is raised 20 deg. For example, satu-
rated air at 40 F raised to 60 F has a relative humidity of 48 per cent; 60 F saturated air
raised to 80 F has a relative humidity of 50 per cent. (See Table 4, Chapter 1.) Thus
a differential thermostat can be used to maintain a nearly constant relative humidity of
50 per cent by holding the dew-point temperature 20 deg below the dry-bulb temperature.
3. The total heat of the air and the water vapor mixed with it varies directly with the
wet-bulb temperature. For example, the occupants of an auditorium give off sensible
heat which tends to raise both the dry-bulb and the wet-bulb temperatures of the space ;
but the occupants also give off moisture which increases the absolute humidity and tends
to further raise the wet-bulb temperature by an amount which is a direct indication of
the heat expended by each occupant in evaporating this water. This relationship is
useful in regulating the total heat, as wet-bulb temperatures can be controlled directly
by means of a thermostat having a sensitive element covered with water-fed wicking,
similar to a wet-bulb thermometer.
For example, the total heat of air at 80 F and 60 per cent relative humidity is the same
as for air saturated at 70 F, i.e., 33.5 Btu per pound, both having a wet-bulb temperature
of 70 F. Air at 80 F and 60 per cent relative humidity (70 F wet-bulb = 33.5 Btu per
pound) reduced to 70 F and 50 per cent relative humidity (58}^ F wet-bulb = 25.2 Btu
per pound, total heat) must give up 8.3 Btu per pound. If the sensible heat and moisture
pick-up in an auditorium is 8.3 Btu per pound of air handled in the conditioning system,
the wet-bulb temperature of the air entering the space must be maintained at 58J^ F to
secure a final condition of 80 F and 60 per cent relative humidity.
Control of Relative Humidity
The following are the most commonly used methods of controlling
relative humidity:
1. A thermostat is located in or at the outlet of a spray-type air conditioner which
maintains a constant saturation temperature of the air leaving the conditioner by varying
the temperature of water entering the suction of the pump^ supplying the spray nozzles,
or by varying the temperature of the air entering the conditioner, or both. The tempera-
ture of the air entering the conditioner may be varied by use of tempering heaters, or by
the proper proportioning of supply and return air entering the conditioner. This thermo-
stat is known as a dew-point thermostat, as it determines the dew-point temperature of
the air introduced into the conditioned spaces. A second thermostat in the room, or in
the path of the air leaving the room, maintains a constant dry-bulb temperature by
varying the amount of sensible heat added to the air leaving the conditioner, or by
varying the volume of air introduced into the conditioned spaces. These two ther-
mostats, in combination, control the dry-bulb and dew-point temperatures, which
accordingly fix the relative humidity.
2. A wet-bulb thermostat is located in the room, or in the path of the air leaving the
roomf to maintain a constant wet-bulb temperature by varying the saturation tempera-
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
ture at the air conditioner outlet. A dry-bulb thermostat is located in the room to
maintain a constant dry-bulb temperature, which in combination with a constant wet-
bulb temperature fixes the relative humidity.
3. A differential thermostat may be used to control relative humidity. This instru-
ment consists of two thermostatic elements, one of which is in the path of the air leaving
the conditioner, and the other under the influence of the dry-bulb temperature in the
room. Instruments of this kind maintain a constant relative humidity by maintaining
a constant difference between the dew-point temperature and the dry-bulb temperature
in the room* (See Item 2 under Air Conditioning Systems.) One thermostatic element
may be equipped with a moistening device to permit it to operate on wet-bulb tem-
peratures. Such an instrument can be used to control the wet-bulb depression and thus
the relative humidity.
4. A humidistat which responds directly to changes in humidity may be used to
maintain a predetermined relative humidity with constant or with varying temperature.
It may do this by varying the dew-point temperature of air leaving a conditioner; by
varying, with dampers, the proportion of moist and dry air; by varying the amount of
moisture otherwise added to the air; or by varying the dry-bulb temperature.
Humidificarion for Residences
The principles underlying humidity requirements and limitations for
residences are summarized in University of Illinois Bulletin No. 481, as
follows:
1. Optimum comfort is the most tangible criterion for determining the air conditions
within a residence.
2. An effective temperature of 65 deg2 represents the optimum comfort for the
majority of people. Under the conditions in the average residence a dry-bulb tempera-
ture of 69.5 F with relative humidity of 40 per cent is the most practical for the attain-
ment of 65-deg effective temperature.
3. Evaporation requirements to maintain a relative humidity of 40 per cent in zero
weather depend on the amount of air inleakage to the average residence, and vary from
practically nothing to 24 gal of water per 24 hours.
4. Relative humidity of 40 per cent indoors cannot be maintained in rigorous climates
without excessive condensation on the windows unless tight-fitting storm sash or the
equivalent is installed.
5. The problems of humidity requirements and limitations cannot be separated from
considerations of good building construction, and the latter should receive serious atten-
tion in the installation of humidifying apparatus.
The following conclusions were drawn from the experimental results
reported in the aforementioned bulletin:
1. None of the types of warm air furnace water pans tested proved adequate to
evaporate sufficient water to maintain 40 per cent relative humidity in the Research
Residence except only in moderately cold weather.
2. The water pans used in the radiator shields tested did not prove adequate to main-
tain 40 per cent relative humidity in a residence similar to the Research Residence when
the outdoor temperature approximated zero degrees Fahrenheit.
Central Fan Air Conditioning Systems
In central fan air conditioning systems as described in Chapters 9 and
22, varying amounts of outside and recirculated air are used, except where
contamination prevents re-use, and in general for obtaining humidity
control under winter conditions heat is supplied to the air after it has
passed the air washer. There are many control variations in use, and
1See Humidification for Residences, by A, P. Kratz (University of Illinois, Bulletin No. 48).
^Sixty-six deg is the optimum winter effective temperature recommended by the A.S.H.V.E. Committee
on Ventilation Standards. See Chapter 2.
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CHAPTER 14 — AUTOMATIC CONTROL
Fig. 9 shows a composite diagram, rather than a system of control for a
single installation. The control valves for a dehumidifying air washer are
shown in Fig. 10. The functions of the control devices shown in Figs. 9
and 10 are as follows:
Winter Operation (With Steam)
1. Thermostat A opens a direct-acting valve in the steam supply to a low-capacity
tempering coil P. The thermostat is set at 35 F.
2. Thermostat B in the path of the air leaving the second tempering coil Q controls a
valve in the steam supply to the coil Q at 45 F.
3. Thermostat C controls the intake M and return air N dampers at 50 F. This
location of thermostat C is primarily for operation with steam heating and at such times
as by-pass damper 0 is closed. See discussion under the heading Spring and Fall Opera-
tion .
FIG. 9.
DIAGRAMMATIC ARRANGEMENT OF VARIOUS PHASES OF CONTROL FOR A
CENTRAL FAN AIR CONDITIONING SYSTEM
4. Humidistat or wet-bulb thermostat D in the return air, acting through a relay,
causes C to call for outside air when the relative humidity rises above 55 per cent or the
wet-bulb temperature rises above 60 F; also, if necessary, thermostat D shuts off the
water supply to the spray heads in the air washer and opens the supply to the flooding
nozzles at the eliminator plates, by operating the three-way valve U (Fig. 10). The
relative humidity must, of course, be changed to suit the requirements. It must be
maintained low enough to avoid condensation on walls or windows.3
5. Thermostat E in the discharge end of the air washer operates a three-way valve
( V, Fig. 10) in the water circulating line so as to cause water to pass through or around
a heating unit in order to produce the correct dew-point temperature by adding any
necessary heat to the water. It may also operate a reverse valve W (Fig. 10) in the steam
supply to the heating unit. The heat added may be only that sufficient to make up the
temperature drop through the washer caused by evaporation. This thermostat is
reverse-acting to prevent over-humidification in case of failure of the motive power.
6. Thermostat F in the fan discharge operates a valve in the steam supply to the
heater R in order to produce the lowest temperature at which air can be introduced into
the conditioned space, without complaints of draft. This varies from 60 F to 70 F,
depending on the velocity through the supply grilles and their location.
"See discussion of condensation in Chapter 7. Also see paper entitled Frost and Condensation on
Windows, by L. W. Leonhard and J. A. Grant (A.S.H.V.E. TRANSACTIONS, Vol. 35, 1929).
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
7. Room thermostat G in a representative location controls a valve in the steam supply-
to the coil or coils S which supply the heat to replace the loss from the conditioned space.
Summer Operation (With Refrigeration)
Thermostats A, B, F, and G all hold their valves closed during summer
temperatures which are above the thermostat settings, although this is
unimportant while no steam is being supplied.
1. Thermostat C, having been set for 50 F, supplies power to open wide the intake
damper and close the return air damper under the higher summer temperatures, and this
power can be passed through a graduating switch to permit manual operation of the
dampers. As the wet-bulb temperature, or total heat, of the outdoor air is now normally
greater than that of the return air, it is desirable in order to keep down cooling costs
to recirculate the maximum amount of air.
2. Humidistat D is by-passed so that power is applied directly to the three-way valve
U (Fig. 10) to prevent shutting off the sprays. This by-pass can be arranged for cutting
in manually, or automatically, with the starting of the refrigerating machinery.
t-To Sprays To Flooding Nozzles
I
Three-way Vatve U-+.\
Three-way VaJve V>*.Q
Reverse Valve W+
Air Flow -4*1
_ -?
I
Cooling Ta-nkT
Heater
Pump-
FIG. 10. CONTROL VALVES FOR A DEHUMIDIFYING AIR WASHER
3. Thermostat E, operating the three-way valve V (Fig. 10), now determines whether
the spray water is to be passed through refrigerated coils or is to be recirculated without
treatment, and thus it regulates the dew-point temperature. It is assumed that steam
and refrigeration are not both turned on at the same time.
4. Thermostat H operates a damper 0 in the by-pass space around the air washer so
as to mix the warmer return air with the cold air leaving the dehumidifier in such pro-
portions as to give the minimum temperature at which air can be introduced into ^the
conditioned space. This might be 70 F for a room temperature of 85 F. A switch
installed in the power line from H should be so connected as to permit keeping damper 0
closed during winter operation.
5. Thermostat G, in addition to operating a valve on the heating unit S, acts as a pilot
for thermostat H so as to retard the action of the latter in closing the by-pass damper
when the temperature in the space is below the desired point.
Spring and Fall Operation
During a considerable part of the year, conditioning can be ^accom-
plished by using all outside air or by mixing it with returned air. For
example, when the total sensible heat gain in an auditorium is 2.4 Btu per
pound of air being treated, outside air will be raised from 60 F to 70 F by
the heat gain. During this period when dry-bulb temperatures are^to be
maintained at, or not much above, 70 F, the gain in sensible heat is the
only factor that need be considered, because it is large in comparison with
the gain in latent heat, except in restaurants and in some classes of
industrial work. The intake and recirculating dampers can then be
operated by thermostat F set at 60 F, It is assumed that such an .outlet
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CHAPTER 14 — AUTOMATIC CONTROL
temperature can be used; if not, the volume of air should be increased.
Thermostat H, being set higher for hot weather, holds by-pass damper 0
open to provide a maximum volume of air. In order to minimize over-
humidifl cation, the air washer and by-pass are arranged so that the return
air stream tends to use the by-pass. However, since dehumidification is
not required, the humidity control is obtained by shutting off the spray
water by humidistat D.
Except for heating-up periods or other times when the heat gain is not
greater than the heat loss, a system of this type can be operated without
artificial heat with outdoor temperatures as low as 40 F. For this reason
it is economical to place a thermostat in the return air near D set to shut
off a valve in the main steam supply to the system at a temperature
about 3 degrees below that desired in the conditioned space. A pilot
thermostat exposed to the outdoor temperature prevents the shut-off on
days colder than 40 F.
As previously stated, there can be many variations from these descrip-
tions, some of which are :
1. Tempering coils may consist of only one bank, P or Q, controlled by thermostat A
or thermostat B. In any case the capacity of the heating unit controlled by the outdoor
temperature must be as low as feasible, otherwise if steam is supplied to it when the out-
door temperature is 30 F, the temperature of the air entering the washer is likely to be too
high to permit maintaining the proper dew-point temperature.
_ 2. Both tempering coils may be omitted and the return air may be mixed with outside
air by thermostat C so as to provide a proper temperature at the washer inlet. In this
case, humidistat D should not act as a pilot.
3. The heating unit for the air washer water may be omitted, and the proper dew-point
temperature maintained by placing thermostat C in the location of E. This requires
either additional heat from the tempering coils or more return air to make up the loss due
to evaporation in the washer.
4. Heating unit 5 may be combined with R in one or two banks and controlled by a
one- or two-point thermostat at F, set for the minimum temperature at which air can be
admitted into the conditioned space. For heating purposes, thermostat G then becomes
a pilot for F so that these heating units are operating at full capacity when the space is
cold, and are throttled by F when no heat is required.
5. Another arrangement is the use of a type of thermostat at F which can operate
at any temperature between a proper minimum and a necessary maximum, de-
pending on the temperature of the space. Thus for winter operation when the room
temperature is 68 F, the blower delivers air sufficiently warm to supply the heat required
under extreme conditions, and when it is 74 F, the delivery will be as cool as possible
without complaint of drafts. A similar device can be used to replace H, and be set to
operate between 60 and 80 F for summer conditions.
6. For summer use, a remote readjustable thermostat can be located at H, and can be
reset by a pilot exposed to the outdoor temperature. Thus as the outdoor temperature
increases, the temperature in the space is maintained at a higher point.
7. A constant portion of the return air may be brought to a point between the air
washer and the blower, and the temperature of the air leaving the washer may be regu-
lated to give the proper result at H. The regulation is accomplished by shutting off one
or more groups of sprays, or by changing the temperature of the spray water until the
proper degree of cooling is secured.
8. Where an air washer large enough to pass all the air handled by the fan is selected,
the by-pass and its damper 0 are not used. The washer sprays must be divided into two
side-by-side sections so that one section can be turned on or off by H to provide the
proper temperature.
9. Where an ejector type heating unit is used for the spray water, a reverse-acting
valve similar to W (Fig. 10) must be placed in the steam supply to be operated by ther-
mostat E. In this case it is usual to install in this steam line another reverse-acting
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
valve to be operated directly by the water pressure in the pump discharge line. This
automatically shuts off the steam when the water circulating pump is not in operation.
10. Based on the fact that the spray water in the air washer pan has practically the
same temperature as the air leaving the washer, dew-point control can be accomplished
by installing thermostat E in the water pan.
11. Where cold well-water is used for dehumidification, it is admitted to the sprays
through a three-way valve similar to V which is operated by thermostat E.
12. Control of steam heat is shown entirely by valves, although it is usual to install a
by-pass damper around each heating unit and to operate it, either with or without a
damper over the face of the heating unit, in conjunction with the valve.
PROBLEMS IX PRACTICE
1 • How may temperature control be obtained in a room heated by a radiator
with a constant steam supply?
By a thermostat handling an individual radiator valve pneumatically or electrically, or
by a self-contained radiator valve.
2 • How may temperature control be obtained in a room heated by a unit
heater?
With constant steam supply, the unit heater motor may be started or stopped by a
thermostat, either directly or through a relay. With intermittent steam supply, opera-
tion of the motor by thermostat can be limited to the time that steam is available, by
using a reverse-acting temperature or pressure limit switch.
3 • How may temperature control be provided in a room heated and venti-
lated by a unit ventilator which includes two ex tended -surf ace units?
Operation of the unit for service during occupancy of the room may be manual, by
switch, or by time clock. When the desired temperature level is reached, the outside
air intake may be controlled by a damper motor coupled with the fan motor circuit by
means of a thermostat. The outside air damper will operate to a given position in
either case.
Air passing through the unit may be preheated through the first heating coil to a definite
temperature by a control valve on the steam supply governed by a temperature controller
reacting to the temperature of the air on the outlet side of the convector. The second
heating coil may provide the necessary heating capacity, and the steam supply to this
coil may be modulated, either manually or automatically, in accordance with the tem-
perature required in the room.
4 • How may temperature control be obtained in a room heated by a duct
system?
Air may enter the room from the central fan system at a predetermined minimum tem-
perature. Heaters placed in the duct to bring the air up to this temperature should be
equipped with face and by-pass dampers which may be adjusted by a positioning damper
motor to give temperature control.
5 • How may temperature be controlled in a room cooled by a unit cooler?
Practice indicates that a thermostat should provide for the automatic operation at all
hours of the fan and control valve on the refrigeration source, but that there be a manual
switch to enable the fan to operate continuously during occupancy.
6 • How may temperature control be obtained in a room cooled by a self-
contained mechanical unit?
The fan operation may be controlled by a manual switch, while a room thermostat in con-
junction with a solenoid valve may regulate the flow of the refrigerant to the coil. The
thermostatic circuit might be operative only when the fans are running; and the com-
pressor might be controlled by refrigerant pressure.
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CHAPTER 14 — AUTOMATIC CONTROL
7 • How may temperature control be obtained in a room heated by an auto-
matically-fired warm air furnace?
A room thermostat might control the combustion unit; and a limit switch in the top of
the furnace unit, when at a low setting of its control might operate the fan whenever
there is a rise of temperature, and when at a high setting of its control it might shut off
the combustion unit. A room humidity control operating a solenoid valve on the water
supply to the humidifier, or operating a relay on the recirculating pump motor to the
humidifier, may be connected in parallel with the fan motor. Humidification may be
supplied only when heat is supplied and when the humidity control acts in conjunction
with a time switch.
8 • How may humidity be controlled in a unit humidifier for a steam or hot
water heating plant?
Since heat is required for evaporation, a temperature limit switch, preferably of the
immersion type, may be placed in the heating supply riser to cause the unit to be in-
operative when heat is not available. A room humidity control will operate a solenoid
valve on the water supply to the sprays. Both the solenoid valve and the humidity
control may be electrically wired in parallel with a fan motor, and be subject to the
temperature limit switch.
9 • Discuss a control system, including control of humidity, for the heating
cycle of a central fan system of air conditioning.
During the heating cycle it is necessary to vary the amount of outdoor air drawn into the
system in accordance with the temperature of that air. It is also advisable to adjust the
volume of return air when mixing it with the outdoor air so that the resultant mixture
will be of constant volume delivered to the preheater coils at some predetermined con-
stant temperature.
By placing a temperature controller in the conditioner just ahead of the preheating coil,
the temperature of the air delivered at that point may be measured, and by connecting
this controller to a damper motor attached to the intake darriper this damper can be
operated by a temperature variation at the controller. The intake damper is so linked
to the return damper that the combined volume of air delivered through the ducts of the
system is constant. At a fall in outdoor temperature, this arrangement will move the
intake damper to a closed position and the return damper to an open position, whereas
the reverse will hold true when there is a rise in outdoor temperature.
If conditions prevent such mechanical linkage, it is possible to use two damper motors
connected so they are operated individually but in inverse ratio.
The operation of the preheating coils should be dependent upon humidity conditions in
the occupied spaces, and the humidity controller should be installed where conditions
are representative of the humidity throughout the section, because air leaving the pre-
heating coils is immediately passed through a spray where it becomes saturated with
moisture. If the air is cold, it will absorb so little moisture that when it is delivered to
the conditioned spaces its relative humidity will be low. When the compensated hu-
midity control calls for additional moisture, the steam control valve in the preheater
line should be opened to allow more steam to flow through the coils.
Whenever the preheating coils are being heated the spray should be in operation, but
when the coils are cut off the air is sufficiently moist and the spray should be closed
down. This necessitates an inter-connection between the control valve on the pre-
heater and the spray pump on the water supply. Water is supplied to the spray during
the heating cycle from a recirculating water tank beneath the sprays.
The reheating coil determines the dry-bulb temperature of the delivered air, so if the
conditioner is equipped with both face and by-pass dampers on this coil it is obvious that
these dampers should be controlled by a thermostat located at some representative
position in the space being supplied with the conditioned air. If this thermostat is in
turn connected with auxiliary apparatus which will vary the damper settings, it will be
possible to pass more or less air through the reheater as the temperature falls or rises.
A low-limit temperature control might also be mounted in the discharge duct as a
precaution against blowing cold air into the space. Such control would actuate the
dampers of the reheater when the duct temperature fell below a predetermined minimum
regardless of the demands of the master controller.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
The amount of steam supplied to the reheater coils should be a function of the position
of the dampers. If the face dampers are closed no heat is required, and to conserve
steam suitable interconnection between the damper motor and the control valve should
be made in order that this valve will close whenever the damper valve is closed. By
adding modulating auxiliary apparatus to the steam valve, it may be made to operate
proportionately to the setting of the dampers.
10 • What is the relation between comfort, economy, and the use of tempera-
ture controls?
As a general rule, a moderate expenditure for control equipment can be justified on the
basis of economy, but the cost of a complete system of individual room control can
ordinarily be only partly so justified and the remainder must be charged to convenience
and comfort. There are, however, many types of systems where the question would not
arise, for without complete control equipment these systems would be unusable.
258
Chapter 15
AIR POULUTION
Sources of Air Pollution, Effects of Air Pollution on Health, Pul-
monary Effects, Occlusion of Solar Radiation, Industrial Air
Pollution, Abatement of Atmospheric Pollution, Smoke Abate-
ment, Dust and Cinder Abatement
THIS chapter considers the hygienic aspects of atmospheric pollution
and the methods by which this pollution may be lessened. Infor-
mation concerning the cleaning of air brought into buildings for ventilat-
ing purposes will be found in Chapter 16, and a discussion of the exhaust-
ing of dusts and toxic gases from factories and industrial plants is con-
sidered in Chapter 21.
The impurities which contribute to atmospheric pollution include
carbon from the combustion of fuels, particles of earth, sand, ash, rubber
tires, leather, animal excretion, stone, wood, rust, paper, threads of
cotton, wool, and silk, bits of animal and vegetable matter, and pollen.
Microscopic examination of the impurities in city air shows that a large
percentage of the particles are carbon. (See Fig. 1, Chapter 16, for size
of impurities in air.)
Dust, Fumes, Smoke
The most conspicuous sources of atmospheric pollution may be
arbitrarily classified according to the size of the particles as dusts, fumes,
and smoke. Dusts are particles of solid matter varying from 1.0 to 150
microns in size. Fumes include particles resulting from chemical pro-
cessing, combustion, explosion, and distillation, ranging from 0.1 to 1.0
micron in size. Smoke is composed of fine soot or carbon particles, less
than 0.1 micron in size, which result from incomplete combustion of
carbonaceous materials, such as coal, oil, tar, and tobacco. In addition to
carbon and soot, smoke contains unconsumed hydrocarbon gases, sulphur
dioxide, sulphuric acid, carbon monoxide, and other industrial gases
capable of injuring property, vegetation, and health.
The lines of demarcation in these three classifications are neither sharp
nor positive, but the distinction is descriptive of the nature and origin of
the particles, and their physical action. Dusts settle without appreciable
agglomeration, fumes tend to aggregate, smoke to diffuse. Particles
larger than one micron will eventually settle out by gravitation ; particles
smaller will remain in suspension as permanent impurities unless' they
agglomerate to sizes larger than one micron.
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Fly-Ash, Cinders
The term fly-ash is usually applied to the extremely small particles of
ash, and the term cinder to the larger particles of coke and ash which are
discharged with the gases of combustion from burning coal.
AIR POLLUTION AND HEALTH
Many kinds of dusts and gases are capable of producing pathological
changes which may cause ill health. The harmful effects depend largely
upon the chemical and physical nature of the impurities, and the con-
centration, length of time, and conditions under which they are breathed.
Dust particles must be minute in size to be inhaled at all, although fairly
large particles may gain access to the upper air passages.
The human body possesses remarkable filtering media for protecting
the lungs. Small hairs which line the nasal passages, and a multitude of
microscopic hairs, called cilia, In the epithelial lining in the bronchial
tubes intercept many of the dust particles before they reach the lungs.
The constant inhalation of dusts in city air irritates the mucous mem-
branes of the nose, throat, and lungs, and eventually may produce dis-
comfort and a series of minor respiratory disorders. The pigmented lung
of the city dweller is an example of the pathological change produced over
a period of years. This condition may be of no clinical importance, but
an exaggeration of it in the coal miner results in anthracosis or dark spots
on the lung due to the presence of pigment in the lymph channels which
impairs the functioning of the lung cells under stress.
Effects of Solids
Bronchitis is the chief condition associated with exposure to thick dust,
and follows upon inhalation of practically any kind of insoluble and non-
colloidal dust. Atmospheric dust in itself cannot be blamed for causing
tuberculosis, but it appears to have a marked influence in aggravating the
disease once it has started. There is, however, quite reliable evidence
that carbon pigment, one of the atmospheric dusts, tends to wall off local
tuberculosis rather than to further its spread.
The sulphurous fumes and tarry matter in smoke are probably more
dangerous than the carbon. In foggy weather the accumulation of these
substances in the lower strata may be such as to cause irritation of the
eyes, nose, and respiratory passages, leading to asthmatic breathing and
bronchitis and, in extreme cases, to death. The Meuse Valley fog
disaster will probably become a classic example in the history of gaseous
air pollution. Released in a rare combination of atmospheric calm and
dense fog, it is believed that sulphur dioxide and other toxic gases from
the industrial region of the valley caused 63 sudden deaths, and injuries
to several hundred persons. Physical examination showed difficult
breathing, rapid pulse, cyanosis, cardiac dilation, and a redness and
inflammation of the mucosa of the nose, mouth, throat, trachea, and
bronchi.
Carbon monoxide from automobiles and from chimney gases con-
stitutes another important source of aerial pollution in busy cities.
During heavy traffic hours and under atmospheric conditions favorable to
concentration, the air of congested streets is found to contain enough CO
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CHAPTER 15 — AIR POLLUTION
to menace the health of those exposed over a period of several hours,
particularly if their activities call for deep and rapid breathing. In open
air under ordinary conditions the concentration of CO in city air is
believed to be insufficient to affect the average city dweller or pedestrian.
Occlusion of Solar Radiation
The loss of light, particularly the occlusion of solar ultra-violet light
due to smoke and soot, is beginning to be recognized as a health problem
in many industrial cities. Measurements of solar radiation in Baltimore1
by actinic methods show that the ultra-violet light in the country was
50 per cent greater than in the city. In New York City2 a loss as great as
50 per cent in visible light was found by the photo-electric cell method,
The effect of air pollution on the health of city dwellers is difficult to
determine, owing to the slowness of its manifestations. The aesthetic and
economic objections to air pollution are so definite, and the effect of air-
borne pollen can be shown so readily as the cause of hay fever and other
allergic diseases, that means and expenses of prevention or elimination of
this pollution have seemed justifiable to the public.
AIR POLLUTION IN INDUSTRY
In many industrial processes, sufficient amounts of dusts, fumes, and
vapors are liberated to be injurious to the health of workers. Some dusts
are poisonous (lead, mercury, arsenic, manganese, and cadmium) and
some act as irritants (silica, steel, iron, and granite). Certain dusts may
produce catarrhal conditions and increase susceptibility to such diseases
as bronchitis, pneumonia, and tuberculosis. Silicious dust is especially
harmful because it has a direct damaging action upon the tissue of the
lungs, but organic dusts, both animal and vegetable (hair, pollen, textile,
and fiber), do not seem to affect the lungs at all, although they may cause
considerable discomfort in the upper respiratory passages to persons
sensitive to them.
Industrial gases and fumes act specifically upon the mucous mem-
branes, the lungs, blood, skin, and eyes. Some extremely poisonous gases
act after very short exposures. Among these are carbon monoxide,
hydrogen sulphide, ammonia, chlorine, bromine, arsine, and cyanogen.
The industrial processes which liberate harmful substances are too
manifold and the effects too diverse to be considered here, where dis-
cussion is limited to the commonest and most serious with which the
ventilating engineer may be confronted, namely, carbon monoxide, lead,
and silica. For a more thorough treatise on the subject reference should
be made to books by Hamilton3, Ro'senau4, and Henderson and Haggard5.
Carbon Monoxide Poisoning
Carbon monoxide is a common form of poisonous industrial gas, met
with in mines, foundries, coke-oven sheds, garages, and houses. Its action
1Effects of Atmospheric Pollution upon Incidence of Solar Ultra-Violet Light, by J. H, Shrader, M. H.
Coblentz and F. A. Korff (American Journal qfPttblic Health, p. 7, Vol. 19, 1929).
^Studies in Illumination, by J. E. Ivea (U. S. Public Health Service Bulletin No 197, 1930).
'Industrial Poisons in the United States, by Alice Hamilton. •
'Preventive Medicine and Hygiene, by Milton J. Roseaau.
Noxious Gases, by Y. Henderson and H. Haggard.
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
is due to the fact that the combining power of carbon monoxide with the
haemoglobin of the red blood corpuscles is about 300 times greater than
that of oxygen. Since the resulting stable combination destroys the
power of the haemoglobin to unite with oxygen in the lungs and to supply
it to the tissues, the effects are due to lack of oxygen, and the symptoms
are those of anoxemia, namely, dizziness, headaches, sleepiness, fatigue,
and, in extreme cases, paralysis and death. The dangerous saturation
level of the blood with carbon monoxide is about 50 per cent. Even as
little as 0.07 per cent in the air will render, in half an hour, one quarter of
the red corpuscles incapable of uniting with oxygen. One to two parts
per 10,000 parts of air is set as a safe limit of pollution which may be
breathed for a long time without producing perceptible symptoms.
Silicosis
Silicosis is a chronic disease of the lungs which results from the local
physio-chemical action of hydrated silica upon the pulmonary tissue,
causing progressive lymphatic fibrosis, and rendering the tissue suscep-
tible to tuberculosis. The disease is slow in evolution, requiring usually a
number of years of exposure. It occurs principally among granite
workers, sand blasters, metal miners, metal polishers, potters, and mill-
stone workers.
Lead Poisoning
Lead poisoning is the most insidious and most common of all industrial
diseases. It occurs principally among lead workers and smelters, lead
miners, potters, painters, typesetters, stereotypers, plumbers, and
workers with glass, gold and silver. Lead, in practically all forms, ^is a
cumulative poison which is absorbed by way of the blood stream, chiefly
from the respiratory tract, but also from the digestive tract and from the
skin. The effect may be either an acute or chronic poisoning. The
principal symptoms are colic, constipation, anemia, headache, anorexia, a
bluish line along the edges of the gums, rheumatic pains, and, in extreme
conditions, paralysis, blindness, insanity, and death.
It has been found6 that 2 mg per day is the smallest dose, by inhalation,
which in the course of years may result in le£d poisoning. Regular
inhalation during the usual working hours of air containing less than
0.2 mg of lead per cubic meter does not seem to produce serious lead
poisoning in individuals of representative industrial groups7.
Prevention
The prevention of industrial hazards from dusts and poisonous gases is
largely a ventilation problem consisting of keeping the impurities in air
down to a safe concentration. As yet there are no generally accepted
standards on which to base the design of the ventilation equipment.
Approximate data on the toxicity of various gases and fumes met with in
industrial establishments are given in Table 1. Column 5, giving the
maximum allowable concentrations for prolonged exposures, was com-
piled from experiments in which most exposures lasted not more than a
•Lead Poisoning, by Thomas Morrison Legge (Journal Royal Society Arts, 1929, Vol. 77, p. 1023).
*What is a Dangerous Quantity of Lead I>ust in Air, by C. M. Sails (Industrial Hygiene Bulletin, New
York State Department of Labor, 1925).
262
CHAPTER 15 — AIR POLLUTION
week, and it is reasonable to assume that over more prolonged exposures
such concentrations would cause pernicious effects.
Much is known concerning the physiological and pathological effects
induced by various types and concentrations of atmospheric pollutants.
In the absence of an accepted standard for safe breathing, and because of
the slow, cumulative effects of certain kinds of air contaminants, the
best procedure is the periodic medical examination of individuals, and the
TABLE 1. TOXICITY OF GASES AND FUMES IN PARTS PER 10,000 PARTS OF AIR*
VAPOR OR GAS
RAPIDLY
FATAL
MAXIMUM
CONCENTRATION
FOB FROM
Yi TO 1 HOUR
MAXIMUM
CONCENTRATION
FOR 1 HOUR
MAXIMUM
ALLOWABLE
FOR PROLONGED
EXPOSURE
Carbon monoxide
40
15-20
10
1
Carbon dioxide
800-1000
Hydrocyanic acid
30
1&
y>
1<
Ammonia
50-100
25
o
Hydrochloric acid gas
10-20
^
Mo
Chlorine
10
<l
Mnn
Hydrofluoric acid gas
2
Mo
Ms
Sulphur dioxide.-
4-5
i/ 1
/2~~-*-
Kft
Hydrogen sulphide
10-30
5-7
2-3
1
Carbon bisulphide.-,.
Phosphene.
Arsine
"20"
2K
11
4-6
Vz
5
1-2
1A
y*
Phosgene.
Over 1A
1A
rs
Nitrous fumes
2J4-7J^
i-iH
•K
Benzene
Toluene and xylene
Aniline
190
190
31-47
31-47
1-1 y>
Mft
Nitrobenzene .
Moo
Xnn
Petrol
243
100-220
Carbon tetrachloride . .
480
240
40
16
Chloroform
250
140
50
2
Tetrachlorethane —
Trichlorethylene -
73
370
1J*
Methyl chloride.
Methyl bromide
1500-3000
200-400
200-400
20-40
70
10
5-10
2
Lead vapor.
5-6
^Original data compiled by Y. Henderson and H. Haggard. (See Noxious Gases, 1927.) Data revised
by T. M. Legge. (See Lessons Learned from Industrial Gases and Fumes, Institute of Chemistry of Great
Britain and Ireland, London, 1930.)
routine measurement and study of the concentration and the physical and
chemical characteristics of the dusts to which those individuals are
exposed.
ABATEMENT OF SMOKE AND AIR POLLUTION
Successful abatement of atmospheric pollution requires the combined
efforts of the combustion engineer, the public health officer, and the
public itself. The complete electrification of industry and railroads, and
the separation of industrial and residential communities would aid
materially in the effective solution of the problem.
In the large cities where the nuisance from smoke, dust and cinders is
263
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
the most serious, limited areas obtain some relief by the use of district
heating. The boilers in these plants are of large size designed and oper-
ated to burn the fuel without smoke, and some of them are equipped with
dust catching devices. The gases of combustion are usually discharged at
a much higher level 'than is possible in the case of buildings that operate
their own boiler plants.
In general, time, temperature and turbulence are the essential require-
ments for smokeless combustion. Anything that can be done to increase
any one of these factors will reduce the quantity of smoke discharged.
Especial care must be taken in hand-firing bituminous coals. (See
Chapter 27.)
Checker or alternate firing, in which the fuel is fired alternately on
separate parts of the grate, maintains a higher furnace temperature and
thereby decreases the amount of smoke.
Coking and firing, in which the fuel is first fired close to the firing door
and the coke pushed back into the furnace just before firing again, pro-
duces the same effect. The volatiles as they are distilled thus have to
pass over the hot fuel bed where they will be burned if they are mixed with
sufficient air and are not cooled too quickly by the heat-absorbing surfaces
of the boiler.
Steam or compressed air jets, admitted over the fire, create turbulence
in the furnace and bring the volatiles of the fuel more quickly into contact
with the air required for combustion. These jets are especially helpful
for the first few minutes after each firing. Frequent firings of small
charges shorten the smoking period and reduce the density. Thinner
fuel beds on the grate increase the effective combustion space in the
furnace, supply more air for combustion, and are sometimes effective in
reducing the smoke emitted, but care should be taken that holes are not
formed in the fire. A lower volatile coal or a higher gravity oil always
produces less smoke than a high volatile coal or low gravity oil used in
the same furnace and fired in the same manner.
The installation of more modern or better designed fuel burning equip-
ment, or a change in the construction of the furnace, will often reduce
smoke. The installation of a Dutch oven which will increase the furnace
volume and raise the furnace temperature often produces satisfactory
results.
In the case of new installations, the problem of smoke abatement can
be solved by the selection of the proper fuel-burning equipment and
furnace design for the particular fuel to be burned and by the proper
operation of that equipment. Constant vigilance is necessary to make
certain that the equipment is properly operated. In old installations the
solution of the problem presents many difficulties, and a considerable
investment in special apparatus is necessary.
Legislative measures at the present time are largely concerned with the
smoke discharged from the chimneys of boiler plants. Practically all of
the ordinances limit the number of minutes in any one hour that smoke of
a specified density, as measured by comparison with a Ringelmann Chart
(Chapter 40), may be discharged. ,
These ordinances do not cover the smoke discharged at low levels by
automobiles, and, although they have been instrumental in reducing the
264
CHAPTER 15 — AIR POLLUTION
smoke emitted by boiler plants, they have, in many instances, increased
the output of chimney dust and cinders due to the use of more excess air
and to greater turbulence in the furnaces.
Legislative measures in general have not as yet covered the noxious
gases, such as sulphur dioxide and sulphuric acid mist, which are dis-
charged with the gases of combustion. Where high sulphur coals are
burned, these sulphur gases present a serious problem.
DUST AND CINDERS
The impurities in the air other than smoke come from so many sources
that they are difficult to control. Only those which are produced in
large quantities at a comparatively few points, such as the dust, cinders
and fly-ash discharged to the atmosphere along with the gases of com-
bustion from burning solid fuel, can be readily controlled.
Dusts and cinders in flue gas may be caught by various devices on the
market, such as fabric filters, dust traps, settling chambers, centrifugal
separators, electrical precipitators, and gas scrubbers, described in later
paragraphs.
The cinder particles are usually larger in size than the dust particles;
they are gray or black in color, and are abrasive. Being of a larger size,
the range within which they may annoy is limited.
The dust particles are usually extremely fine; they are light gray or
yellow in color, and are not as abrasive as cinder particles. Being ex-
tremely fine, they are readily distributed over a large area by air currents.
The nuisance created by the solid particles in the air is dependent on
the size and physical characteristics of the individual particles. The
difficulty of catching the dust and cinder particles is principally a function
of the size and specific gravity of the particles.
Lower rates of combustion per square foot of grate area will reduce the
quantity of solid matter discharged from the chimney with the gases of
combustion. The burning of coke, coking coal, and sized coal from which
the extremely fine coal has been removed will not as a general rule produce
as much dust and cinders as will result from the burning of non-coking
coals and slack coal when they are burned on a grate.
Modern boiler installations are usually designed for high capacity per
square foot of ground area because such designs give the lowest cost of
construction per unit of capacity. Designs of this type discharge a
large quantity of dust and cinders with the gases of combustion, and if
pollution of the atmosphere is to be prevented, some type of catcher must
be installed.
Dust and Cinder Catchers8
The various types of dust and cinder catchers available today can be
divided into six general classes:
1. Settling chambers.
2. Dust and cinder traps.
3. Centrifugal separators.
•See Smoke and Dust Abatement, by M. D. Engle (A.S.H.V.E. TRANSACTION, Vol. 37, 1931).
265
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
4. Electrostatic precipitators.
5. Gas scrubbers.
6. Fabric filters.
The selection of the proper type of catcher calls for a careful study of
the material to be caught and the draft and space available. After
installation, constant vigilance is necessary to keep the catchers in proper
working condition if satisfactory operation is to be obtained.
If possible, the dust or cinder catcher should be installed on the inlet
side of the induced draft fans because the dust and cinders in the gases
seriously erode the wheels of the fans, the inlet connectioxis and the
scrolls. Where the induced draft fans operate at high tip speeds and no
catchers are installed, it is not uncommon for the fans^to require major
repairs within one year and complete replacement within five years.
Settling Chambers
Probably the oldest form of dust catcher is the settling chamber,
which generally consists of a large-sized, gas-tight space into which the
dust-laden gases are discharged before being delivered to the chimney.
The velocity of the gas should be reduced to a point where the larger and
heavier particles will be precipitated by gravity. For good operation, the
velocity of the gas should be reduced to a maximum of 2 f ps. The bottoms
of the chambers should be provided with dump plates through which the
collected dust can be removed. Because these chambers are not effective
in removing the finer dust particles they have been practically superseded
by smaller and less costly devices.
Traps, Catchers, Precipitators
Various types of traps have been devised. In general they all depend
upon breaking the gas up into thin ^strata and subjecting those thin
strata to several abrupt changes in direction. The dust is thrown out
of the gas stream into specially shaped pockets, or impinged against a
roughened surface. The trapping pockets are drained into a hopper
below with a small quantity of gas and the dust settles out by gravity due
to the low velocity in the hopper. In the roughened surface type, various
sections of the trap are closed off at intervals by means of dampers and
the dust is shaken off the roughened surface into a hopper below.
These devices work very well in catching large size dust and cinders and
trap much of the fine dust. They have been used most extensively on
stoker-fired installations. They have the advantages of low pressure
drop, relatively small space requirements, and low first cost.
Centrifugal catchers obtain separation by projecting the particles
tangentially out of the gas stream. The effectiveness of this type of
catcher varies directly as the specific weight of the dust and as the square
of the tangential velocity, and inversely as the radius of rotation.
Electrostatic precipitators are used for catching fine dust. These
precipitators consist of dust-tight chambers in which are suspended rein-
forced concrete slabs on about 10-in. centers. Between the slabs are
suspended bare metal rods. High- voltage unidirectional current^ is
applied to the reinforcing rods in the concrete slabs acting as positive
electrodes, the bare rods acting as negative electrodes. The dust-laden
266
CHAPTER 15 — AIR POLLUTION
gas flows horizontally through the precipitator and the dust particles
migrate toward the concrete slabs to which they adhere and then fall or
are scraped off into the dust hoppers below.
Gas Scrubbers
Wet scrubbers have been used for many years for removing dust from
gases. A number of different types of scrubbers are now being built for
removing dust from boiler flue gases. One type depends upon saturating
the gas and washing the dust out of suspension by a spray of water. For
best results with this type, the water should be atomized into as fine a
spray as possible.
Another type depends upon splitting the gas into thin strata and
subjecting these strata to a number of abrupt changes in direction,
throwing the dust against the wet surfaces. The main problem in develop-
ing a satisfactory wet dust catcher is to find suitable materials of con-
struction that will resist the corrosive action of the wash water for a
reasonable length of time.
Fabric Filters
Filters of many kinds have been used with variable success. The
filter bags are made of cotton, wool or asbestos fabric. The fabrics used
in these filters do not withstand the temperatures at which gases are
usually discharged from the boilers, and hence the gases must be cooled by
some means. Surface coolers or water sprays can be used for reducing the
gas temperatures.
One of the serious objections to all of these dust catchers is the relatively
high cost of installation and maintenance, and the space required for
installation.
Disposal of Dust and Cinders
Even after the dust and cinders have been caught, the disposal of the
material caught presents a serious problem. The cinders discharged with
the gases from stoker-fired boilers are usually very high in carbon and
contain from 50 to 80 per cent as much heat per pound as the coal which
is being burned. It is possible, and usually economical, to burn these
cinders. They cannot be satisfactorily mixed with the coal in the stoker
hopper but they can be blown into the furnace over the stoker fuel bed
and burned satisfactorily. If a sufficient quantity of cinders is caught, a
small unit pulverizer can be installed to prepare them for burning over
the stoker fuel bed. The same pulverizer can be used for coal at times of
peak load and will materially increase the capacity of the fuel-burning
equipment for the boiler to which it is connected.
No satisfactory market has been developed for the dust caught from
pulverized coal installations, but the possibilities are being investigated
and it seems likely that in the future this material will have a market
value that will go a long way toward paying the fixed charges on the cost
of catching it.
The distribution of dust in the gas entering and leaving the dust and
cinder catchers is not uniform and is different in practically every in-
267
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
stallation, and varies widely with changes in furnace conditions. In
order to obtain a representative sample it is necessary to traverse the
inlet and outlet of the catcher with a sampling tube which faces into the
gas flow. The velocity of the gas into the sampling tube must be the
same as the velocity of the gas in the duct at the instant the sample is
taken. The swirls and eddy currents in the ducts make it difficult to
obtain consistent readings, but if the test is conducted by some one of
experience, an indication of the approximate efficiency can be obtained.
Nature's Dust Catcher
Nature has provided means for catching solid particles in the air and
depositing them upon the earth. A dust particle forms the nucleus for
each rain drop and the rain picks up dust as it falls from the clouds to the
earth. In fact, without dust in the air to form the nuclei for rain drops it
would never rain, and the earth would be continually enveloped in a cloud
of vapor.
PROBLEMS IN PRACTICE
1 • What is a micron?
A micron equals 0.001 millimeter or approximately Jisoo in.
2 • Distinguish between dusts, fumes, and smokes.
Solid particles ranging in size from 1.0 micron to 150 microns are called dusts.
Particles resulting from sundry chemical reactions and ranging from 0.1 to 1.0 micron in
size are called fumes.
Carbon particles less than 0.1 micron in size which generally arise from the incomplete
combustion of such materials as coal, oil, or tobacco are called smokes.
3 • What are some of the more important physical properties of these various
groups of foreign bodies which are of importance in ventilation?
In slowly moving air, dusts tend to settle out by gravity without agglomerating to form
larger particles; fumes have the tendency to form larger particles which will settle when
they attain the size of approximately 1.0 micron ; while smokes tend to diffuse and remain
in the air as permanent impurities.
4 • Why is atmospheric pollution an important engineering problem?
a. Certain impurities, when present in too great concentrations, cause ill health or even
death.
b. High concentrations of solids occlude solar radiations.
c. Some materials cause permanent injury to parts of buildings, as sulphur fumes corrode
exposed metal.
d. Extra cleaning expense is incurred in dusty localities.
e. Internal combustion engines are damaged by abrasive dusts.
5 • How may the hazards of dust-producing industrial operations best be
curtailed?
By providing mechanical exhaust ventilation sufficient to keep dust concentration at a
safe level (see Table 1) and then removing foreign bodies to reduce the pollution of out-
side air.
6 • How may the pollution of the atmosphere be lessened?
By compelling industrial plants to install dust catching and smoke controlling devices.
In many cities the domestic heating plant is one of the most serious offenders, but these
268
CHAPTER 15 — AIR POLLUTION
plants are too small to justify the installation of dust catchers. Public education in
improved firing methods would be of considerable help in this field.
7 • Compare the dry and wet types of dust catchers.
The dry types are very effective in removing the larger dust particles but the smaller
particles generally pass through other kinds than the electric precipitator, The dry
types also require considerable space and therefore sometimes introduce resistance to
the flow of air. The wet types are effective in removing some of the smaller dusts and the
water-soluble gases. The principal disadvantage of the washer is its short life caused
by the corrosive action of the wash water.
8 • What size particles are detrimental to health?
While fairly large particles may enter the upper air passages, those found in the lungs
are seldom more than 10 microns in size, and comparatively few of them are more than
5 microns. It is agreed that particles between J^ and 2 microns may be harmful; some
authorities place the upper limit at about 5 microns, and some incline to extend the
lower limit to 0.1 of a micron.
9 • Is the shape of the particle of any significance?
Hard particles with sharp corners or edges have a cutting effect on the delicate mucous
membranes of the upper respiratory tract which may lower the resistance of the nose and
throat to acute infections. This is aggravated by the irritating effects of some chemical
compounds which may be taken in with the air and which act to reduce resistance.
10 • What are the principal meteorological effects of smoke and dust?
a. The reduction in the amount of light received. Measurements have shown that
visible light may be as much as 50 per cent less intense in a smoky section of a city than
in a section that is free from smoke. Ultra-violet light is reduced as much or more, and
in some cases is cut out entirely for a time.
b. Smoke and dust aid in the formation and prolongation of fogs. City fogs accumulate
smoke and become darker in color and very objectionable. The sun requires a longer
time to disperse them, and when the water is evaporated, there is a rain of smoke and
soot particles that have been entrained.
11 • Why has not smoke abatement been more effective?
Because communities have not been made sufficiently aware of the possibilities of
burning high volatile fuels smokelessly and of separating cinder and ash from the stack
gases to a degree that will prevent a nuisance.
12 • Is the abatement of dust and cinders important?
Yes. Only a small percentage of the solid emission from stacks is smoke, in the accepted
popular sense; the remainder is fly-ash and cinders. While black smoke is disagreeable
and its tarry matter and carbon particles soil anything with which they come in contact,
the cinders and some of the ash are hard and destructive. They also, together with
dusts from industrial processes, make up the hard, sharp, irritating, air-borne solids
that are breathed by individuals not working in a dusty mill or factory.
13 • Are air-borne impurities causative factors in hay fever, bronchial asthma,
and allergic disorders?
Yes. Recent medical investigations indicate that 90 per cent of seasonal hay fever and
40 per cent of bronchial asthma are caused by air-borne pollens, tree dusts, and other
allergic irritants.
14 • Name some essential requirements for the smokeless combustion of fuels.
Time, temperature, and turbulence. A study of these factors is usually of value in
overcoming a smoke nuisance.
269
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
15 • What is the Ringelmann Chart Method of comparing smoke densities?
See Chapter 40. The Ringelmann Chart consists of four cards ruled with lines having
different degrees of blackness. These cards, together with a white card and a black one,
are hung in a horizontal row 50 ft from the observer. At this distance the lines become
invisible and the cards appear to be different shades of gray, ranging from white to black.
The observer, by matching the cards against the shades of smoke coming from a stack, is
able to estimate the blackness of the smoke as compared with the chart.
270
Chapter 16
AIR CLEANING DEVICES
Requirements of an Air Cleaner, Types, Air Washers and Scrubbers,
Viscous Type Filters, Dry Air Filters, Air Filter Installations
THE removal of impurities from air brought into a building for
ventilating or air conditioning purposes is the function of any air
cleaning or filtering device. These impurities include carbon (soot) from
the incomplete combustion of fuels burned in furnaces and automobile
engines, particles of earth, sand, ash, automobile tires, leather, animal
excretion, stone, wood, rust and paper, threads of cotton, wool and silk,
bits of animal and vegetable matter, bacteria and pollen. Microscopic
examination shows that the character of the impurities varies with the
locality, but as a rule carbon forms the greater part of them while the
total is somewhat proportional to the state of industrial activity and the
wind intensity. Additional information on sources of air pollution will
be found in Chapter 15.
Observations have shown that practically all atmospheric impurities
are less than 5 microns in size. (One micron equals 0.001 millimeter or
approximately 0.00004 in.) The size and composition of each individual
particle determines its buoyancy and consequently the length of time it
will remain in suspension. The chart, Fig. 1, shows graphically the sizes
of impurities found in the air, and other related data.
To estimate the probable dust load for air filter installations, the
following approximate averages of atmospheric dust concentration may
be used (7000 grains equal 1 Ib) :
Rural and suburban districts 0.2 to 0.4 grains per 1000 cu ft
Metropolitan districts 0.4 to 0.8 grains per 1000 cu ft
Industrial districts 0.8 to 1.5 grains per 1000 cu ft
REQUIREMENTS OF AN AIR CLEANER
To fulfill the essential requirements of clean air, an air cleaner should:
1. Be efficient in the removal of harmful and objectionable impurities in the air, such
as dust, dirt, pollens, bacteria.
2. Be efficient over a considerable range of air velocities.
3. Have a low frictional resistance to air flow; that is, the pressure drop across the
filter, measured in inches of water, should be as low as possible.
4. Have a large dust-holding capacity without excessive increase of resistance, or
have ability to operate so as to keep the resistance constant automatically.
5. Be easy to clean and handle, or dean itself automatically.
ft. Leave the air passing through the cleaner free from entrained moisture or charging
liquids used in the cleaner.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
The A.S.H.V.E. Standard Code for Testing and Rating Air Cleaning
Devices Used in General Ventilating Work1 explains how such devices are
rated by (1) capacity in cubic feet of air handled per minute, (2) resistance
01 AM.
OF
PAR-
TICLES
IN
MIC ROMS
SCALE OF
ATMOSPHERIC
IMPURITIES
RATE OF
SETTLIK&
IN FP.M.
FOR
SPHERES
OF
DENSITY 1
AT 70 °F.
NUMBER
OF PAR-
TICLESW
ONE CUJT
SURFACE
AREA IN
SQUARE
INCHES
LAWS OF SETTLING
IN RELATION TO
PARTICLE SIZE
(LIMES OF DEMARCATION APP«Ot.) ;
AIR CONTAINING
.0006 GRAINS OF
IMPURITIES PER
8000
eooo
Lu — _!__ ^ [_j
—
1750
PARTICLES FALL WITH !
INCREASING VELOCITY
4000
^ooo
1000
800
600
400
200
10O
80
60
40
eo
10
i
! '
790
.075
.000365
| PARTICLES SETTLE WITH CONSTANT VELOCITY
C = 24.9V Ds,
S
C-V«locity ft/mm.
d°Diam of par- i
tide m cm
D = Diatn of par-
tick m Microns
r» Radius of par-
ticle in cm
g-981 cm./Sfcc4
acceleration
s,-Dtnsit_y of
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FIG. 1. SIZES AND CHARACTERISTICS OF AIR-BORNE SOLIDS
in inches of water at rated capacity, (3) dust arrestance, the percentage
relationship expressing dust removal efficiency at rated capacity, (4)
reconditioning power, the energy necessary to operate the mechanism of
lAdopted 1934 by A.S.H.V.E. See Chapter 41.
272
CHAPTER 16 — AIR CLEANING DEVICES
an automatic air cleaning device, and (5) dust holding capacity, the
amount by weight of standard dust which a non-automatic air cleaning
device will retain before reconditioning is necessary.
TYPES OF AIR CLEANERS
According to the Code, the following four classifications are given the
devices :
Class A. Automatic Type: In general all air cleaning devices which use power to
automatically recondition the filter medium and maintain a non- vary ing resistance to
air flow.
Class B. Low Resistance Non- Automatic Type: Air cleaning devices for warm air
furnaces, unit ventilating machines and similar apparatus and installations in which a
maximum of not more than 0.18 in. water gage is available to move air through the air
cleaning device.
Class C. Medium Resistance Non- A utomatic Type: Air cleaning devices for systems
in which a maximum of not more than 0.5 in. water gage is available to move air through
the air cleaning device.
Class D. High Resistance Non- A utomatic Type: Air cleaning devices for the air
intake of compressors, internal combustion engines, and the like, where a pressure of
1.0 in. or more water gage is available to move air through the air cleaning device.
Air cleaners may be also classified as follows:
1. According to principle of air cleaning.
a. Air washers.
b. Viscous air filters.
(1) Unit type.
(2) Automatic type.
c. Dry air filters.
2. According to application.
a. For central fan systems of ventilation and air conditioning. Filters of the
automatic or semi-automatic type are usually recommended and are installed
in a central plenum chamber.
b. For unit ventilators. Filters of viscous unit or dry type, installed at inlet of
individual units.
c. For window installations. Self-contained units consisting of fan and filter,
usually dry type , adapted to be placed in the ordinary window.
d. For warm-air furnaces. Unit type viscous or dry filters placed in small plenum
chamber of warm-air house heating systems.
e. For compressors and Diesel engines. Unit type viscous or dry filters, installed at
air intake of compressors and Diesel engines.
f. For compressed air lines. Unit type viscous or dry filters.
With the growing congestion of large cities and an industrial growth
throughout the entire country, the percentages of foreign material in the
air, such as soot or carbon, which are unaffected by an air washer type of
air cleaner, have increased. This has brought about the development of
the viscous and dry type air filters which are part of many ventilating and
air conditioning systems.
AIR WASHERS AND SCRUBBERS
Information on air washers will be found in Chapter 11.
Scrubbers have not been used very extensively in the past for cleaning
273
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
air for ventilating purposes. However, new types have been developed
which appear to have possibilities for cases where the air to be cleaned is
extremely dirty or where a higher degree of cleanliness is desired than can
be obtained with an air washer.
VISCOUS TYPE FILTERS
The principle of air cleaning used in viscous filters is that of adhesive
impingement. Dust and dirt in the air, especially soot and carbons, are
trapped and retained by successive impingements on coated surfaces.
While the arrangements of filtering media and the kind of materials used
are almost unlimited, there are certain rather definite requirements for a
practical commercial filter.
Investigations in this country and abroad demonstrate that the first
impingement of dust laden air on a viscous coated surface removes about
60 per cent of the dust, the next impingement takes 60 per cent of what
then remains — that is, 24 per cent — and the next impingement removes
9.6 per cent. To secure maximum efficiency, it is necessary to divide the
air into innumerable fine streams, as the more intimately and freely the
air is brought into contact with the viscous-coated media the better will
be the cleaning.
The binding liquid used with viscous filters should have the following
properties :
1. Its surface tension should be such as to produce a homogeneous film-like coating
on the filter medium.
2. The viscosity should vary only slightly with normal changes of temperature.
3. It should be germicidal in its action to prevent the development of mold spores
and bacteria on the filter media.
4. The liquid should flow freely at low temperatures.
5. Evaporation should not exceed 1 per cent.
6. It should be fireproof.
7. It should be odorless.
Viscous Unit Filters
In the unit type viscous filter, the filtering media are arranged in units
of convenient size to facilitate installation, maintenance, and cleaning.
Each unit consists of an interchangeable cell or replaceable filter pad and
a substantial frame which may be bolted to the frames of other like units
to form a partition between the source of dusty air and the fan inlet.
The necessary washing, draining, and recharging equipment should be
installed near each group of unit filters, with hot water and sewer con-
nections provided.
To secure greater dust holding capacity and a practically constant
resistance and air volume, the filter media are usually placed in the
direction of air flow, with progressively finer filter densities determined
by the percentage of dust impinged. This arrangement provides relatively
large spaces for the collection of dirt in the front of the filter where the
bulk of the dust is taken out without undue increase in resistance, while
at the back of the filter the openings are smaller to secure high efficiency
in the removal of the finer dust particles.
The resistance of a well-designed unit filter of the adhesive impinge-
274
CHAPTER 16 — AIR CLEANING DEVICES
merit type usually depends upon the velocity at which the air is handled
and upon whether the unit is clean or dirty. The cleaning efficiency ^of
the unit is usually highest after it has accumulated a certain portion of its
maximum load of dirt because some dust collected in the cell acts as an
efficient medium for the further seizing of solids from the air. By periodi-
cally cleaning a predetermined number of cells, the resistance and capacity
of a built-up filter may be held at any desired figure. The frequency of
cleaning any unit filter installation depends upon the dust concentration
0.30 &
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FIG. 2. CHART SHOWING CHANGE IN RESISTANCE DUE TO DUST ACCUMULATION
0.40
700 750 800 850 900
Cubic Feei of Air-ThroiKjh Fitter per Minule
950 1000
FIG. 3. RESISTANCE TO AIR-FLOW OF A TYPICAL UNIT Am FILTER
of air being cleaned, and on the amount of dirt which can be accumulated
in the filter medium without causing excessive resistance.
Filters consisting of inexpensive frames of cardboard or similar material
filled with viscous-coated glass wool or steel wool are available. Because
of their construction these units may be discarded when dirty and replaced
with new units at relatively little expense. They are used in general
ventilation work and with warm air furnaces and other installations where
first cost and low resistance to air flow are essential. The operating
characteristics of these units conform in general with those of the rigid
frame type.
Viscous Automatic Filters
The principle of air cleaning used in the viscous automatic filters is
the same as in the unit filters. The removal of the accumulated dust,
275
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
however, is done automatically instead of by hand. The automatic clean-
ing and recoating of these filters is based on the principle that the viscous
fluid itself will perform the cleaning function, thereby eliminating a sepa-
rate washing agent. The dust collected by the filter thus is deposited
finally in the bottom of the viscous fluid reservoir from which it may be
removed by different methods, depending on the design of the filter.
There are three general types of automatic filters. They are differentiated
from each other according to the process of self-cleaning and renewing
of the viscous coating used by each type, as follows:
1. The filter medium has the form of an endless curtain suspended vertically, with its
lower portion submerged in a viscous fluid reservoir. The curtain rotates slowly through
this bath, thus performing the cleaning and recoating of the filter medium.
2. The filter screen is arranged in the form of shelves or cylinders, and the viscous
fluid is flushed through all parts of the medium in a direction opposite to the air flow,
3. The filter medium is arranged vertically and is stationary. The viscous fluid is
flushed from above over the medium, while the air flow is stopped.
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FIG. 4. MAINTENANCE CHART FOR UNIT TYPE Viscous FILTERS
The washing and renewing process in automatic filters usually is inter-
mittent. It is accomplished by an electric motor or by other motive
power and is controlled by manual or by automatic timing devices. The
operating cycle is of a predetermined frequency and should be so timed
as to insure a constant static pressure drop across the filter. The customary
resistance to air flow is i^-in. water gage at an air velocity of 500 fpm,
measured at the filter entrance. Automatic viscous filters are made up in
units which are delivered either fully assembled or in parts to be assem-
bled at the point of installation,
DRY AIR FILTERS
Dry air filters, in which dust is impinged upon or filtered through
screens made of felt, cloth, or cellulose, are available in various types.
These filters require no adhesive liquid, but depend on the straining or
screening action of the filtering medium. Because of the close texture
276
CHAPTER 16 — AIR CLEANING DEVICES
of the filtering media used in most of the dry filters, the surface velocity,
or velocity of the air entering the media, ranges between 10 and 50 fpm,
depending on the nature and texture of the fabric. This necessitates a
relatively large screen surface, and the filter media are usually arranged
in the form of pockets to bring the frontal area within customary space
requirements.
As in viscous unit filters, an average constant resistance and air volume
may be obtained by periodic reconditioning or renewal of the filter
screens. Since some materials suitable for dry filtering media are affected
considerably by moisture which tends to cause a rapid increase in resis-
tance, they should be treated or processed to minimize the effect of
changes in humidity.
Filters using felt and similar materials as filter media depend upon
vacuum cleaning for reconditioning. A special nozzle, operated from a
portable or stationary vacuum cleaner, is shaped to reach all parts of the
filter pockets. Permanent filter media should be capable of withstanding
repeated vacuum cleanings without loss in dust removal efficiency.
While most dry filters are cleaned by replacing an inexpensive filter sheet,
the useful life of these sheets often may be lengthened by vibrating or
vacuum cleaning.
INSTALLATION METHODS
The published performance data for all air filters are based on straight
through unrestricted air flow. Filters should be installed so that the face
area is at right angles to the air flow whenever possible. Eddy currents
and dead air spaces should be avoided and air should be distributed
uniformly over the entire filter surface, using baffles or diffusers if neces-
sary.
The most important requirements of a satisfactory and efficiently
operating air filter installation are:
1. The filter must be of ample size for the amount of air it is expected to handle. Aii
overload of 10 to 15 per cent is regarded as the maximum allowable. When air volume is
subject to increase, a larger filter should be installed.
2. The filter must be suited to the operating conditions, such as degree of air clean-
liness required, amount of dust in the entering air, type of duty, allowable pressure drop,
operating temperatures, and maintenance facilities.
3. The filter type should be the most economical for the specific application. The
first cost of the installation should be balanced against depreciation as well as expense
and convenience of maintenance.
The following recommendations apply to filters and washers installed
with central fan systems:
1. Duct connections to and from the filter should change size or shape gradually to
insure even air distribution over the entire filter area.
2. Sufficient space should be provided in front as well as behind the filter to make it
accessible for inspection and service. A distance of two feet may be regarded as the
minimum.
3. Access doors of convenient size should be provided in the sheet metal connections
leading to and from the filters.
4. All doors on the clean air side should be lined with felt to prevent infiltration of
unclean air. All connections and seams of the sheet metal ducts oh the clean air side
should be as air-tight as possible.
277
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
5. Electric lights should be installed in the chamber in front of and behind the air filter.
6. Air washers should, whenever possible, be installed between the tempering and
heating coils to protect them from extreme cold in winter time.
7. Filters installed close to air inlet should be protected from the weather by suit-
able louvers, in front of which a large mesh wire screen should be provided.
8. Filters should have permanent indicators to give a warning when the filter re-
sistance reaches too high a value.
REFERENCES
Testing and Rating of Air Cleaning Devices Used for General Ventilation Work, by
Samuel R. Lewis (A.S.H.V.E. Journal Section, Heating, Piping and Air Conditioning,
May, 1933).
Fundamental Principles in the Design of Dry Air Filters, by Otto Wechsberg
(A.S.H.V.E. Journal Section, Heating, Piping and Air Conditioning, April, 1933).
Operation and Maintenance of Air Filters, by W. G. Frank (Heating, Piping and Air
Conditioning, May, 1931).
Size and Characteristics of Air-Borne Impurities, by W. G. Frank (Heating, Piping
and Air Conditioning, January, 1932).
Determining the Quantity of Dust in Air by Impingement, by F. B. Rowley and
John Beal (A.S.H.V.E. TRANSACTIONS, Vol. 35, 1929).
A Study of Dust Determinators, by F. B. Rowley and John Beal (A.S.H.V.E. TRANS-
ACTIONS, Vol. 34, 1928).
Design and Application of Oil-Coated Air Filters, by H. C. Murphy (A.S.H.V.E.
TRANSACTIONS, Vol. 33, 1927).
Determining the Efficiency of Air Cleaners, by A. M. Goodloe (A.S.H.V.E. TRANS-
ACTIONS, Vol. 30, 1924).
PROBLEMS IN PRACTICE
1 • What is meant by air filter performance characteristics?
The factors that determine the performance of an air filter, which are:
(1) efficiency in dust removal, (2) operating resistance, (3) dust holding capacity. In a
properly designed filter these factors are balanced to obtain the desired characteristics
for a given application. Since the requirements vary for different kinds of air cleaning
service, it is necessary to have filters of different types to meet the various conditions.
2 • What are the advantages of viscous filters?
The principal advantage of the viscous filter is its large dust holding capacity. The dust
accumulation is distributed through the depth of the filtering medium rather than upon
the surface as in the dry types, which makes it possible for viscous filters to handle
heavy dust concentrations without excessive resistance. Since its efficiency and resis-
tance are based on maximum air velocities of from 300 to 500 ft per minute through the
filter, the viscous filter consumes the minimum amount of space for a given air volume.
3 • What are the advantages of dry filters?
Dry filters are more efficient in the removal of fine dust particles from the air, and some
types will eliminate even as much as 60 per cent of the smoke particles. Dry filters also
are easily and conveniently maintained by vacuum cleaning, vibrating, or renewing the
filtering medium. _ i
4 • If an air washer is used for cooling and humidity control in an air con-
ditioning system, is a filter needed?
An air filter is desirable in conjunction with an air washer because of the large amount of
soot in the air which, due to its greasy and amorphous nature, is not readily trapped in
278
CHAPTER 16 — AIR CLEANING DEVICES
an air washer. Filters should be placed between the washer and the air intake so that
all the dirt will be collected at one point to simplify maintenance, to protect all the
equipment in the system, and to prevent contamination of the water used in the washer.
5 • Is an air filter needed with an extended surface type heat exchanger?
An air filter is essential with an extended surface heat exchanger in order to maintain its
efficiency, for without this protection dust particles will adhere to the exposed surfaces,
and gradually build up a deposit to the point where the efficiency will be impaired and the
resistance increased by restricting the air passage.
6 • What is the proper location of a filter in relation to the fan?
A filter will operate equally well whether placed on the suction or discharge side of the
fan. It has become standard practice, however, to locate the filter on the fan inlet side
because there it has: (1) simpler duct connections, (2) reduced static pressure losses,
(3) more even air distribution over the entire filter area. Where an exceptionally high
efficiency in dust removal must be maintained, it is often advisable to place the filter on
the discharge side of the fan so there can be no infiltration of unclean air.
7 • What instruments and apparatus are required for determining the pollen
concentration in air by means of the settling method?
A microscope with a field of know area and a glass slide coated with a viscous material.
8 • Describe the procedure for determining the pollen concentration in air by
means of the settling method.
A glass slide coated with a viscous material is placed for a period of 24 hours in a hori-
zontal position in the atmosphere to be tested. The slide is then removed and placed
under the microscope, and pollen counts are made of approximately 25 fields over the
area of the glass slide. Having determined the count over a definite area, as for example,
1 sq cm, and finding the settling rate of the average particles from the chart, Fig. 1, the
concentration in parts per cubic yard can be calculated.
9 • The resistance to ah* flow of a unit air filter is found to be 0.4 in. of water.
The volume of air passing through the filter is 1000 cfm at a velocity of 200 fpm.
What would be the filter area required in order to reduce the pressure drop
across the filter from 0.4 in. of water to 0.16 in. of water?
Referring to Fig. 3: The resistance is substantially proportional to the square of the
velocity, or
Q = It
R« V,}
0.4 2002
0.16 722
F22 = 16,000
F2 - 126.5 fpm
Q = AV
1000 = 126.5 A
The filter area would be increased from 5 sq f t to 7.91 sq ft.
10 • A ventilating system complete with filters has a fan which, when operating
at 400 rpm and delivering air at 1 in. of water total static pressure, requires an
input of 3 horsepower. After the system operates for a time, the pressure drop
across the filter caused by the clogging action of the collected dust and dirt
increases from 0.1 in. of water to 0.4 in. of water. To maintain the original
279
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
rate of air delivery with the increased static pressure, at what speed must the
fan be run and what horsepower will be required?
Static pressure after clogging of filter = 1 -j- (0.4 — O.lj = 1.3 in. of water.
The static pressure varies as the square of the fan speed. Therefore, if X is the fan speed
after the static pressure increases:
1.3
1 V 400
X = 456 rpm.
The horsepower varies as the cube of the fan speed. Therefore, if Y is the horsepower
after the static pressure increases:
456 \3
__
3 V 400 /
F = 4.44 horsepower.
To maintain the original rate of air delivery with the increased static pressure, the fan
speed must be increased from 400 to 456 rpm, and the horsepower from 3 to 4.44.
280
Chapter 17
FANS AND MOTIVE POWER
Performance, Fan Efficiency, Characteristic Curves, Selection of
Fans, Controls, Designation of Fans, Motive Poiver, Electric Power
FANS are used for producing air flow except where positive displace-
ment is required, in which case compressors or rotary blowers are
used. Fans are classified according to the direction of air flow as (1)
axial flow or propeller type if the flow is parallel with the axis, and (2)
radial flow or centrifugal type if the flow is parallel with the radius of
rotation.
Axial flow fans are made with various numbers of blades of a variety
of forms. The blades may be of uniform thickness (sheet metal), either
flat or cambered, or may be of varying thickness of so-called aerofoil
section (airplane propeller type). Where an axial flow fan is intended for
operation at comparatively high pressures the hub sometimes is enlarged
in the form of a disc and the fan is known as a disc fan.
Radial flow or centrifugal fans include steel plate fans, pressure blowers,
cone fans, and the so-called multiblade fans. All the foregoing types have
variations which may be obtained by modification of the proportions or
change in the curvature and angularity of the blades. The angularity of
the blades determines the operating characteristics of a fan: a forward
curved blade is found in a fan having slow speed operating characteristics,
while a backward curved blade is found in a fan having high speed
operating characteristics.
A wide variation exists in the demands which have to be met by fan
installations. A fan may be required to move large quantities of air
against little or no resistance or it may be required to move small quanti-
ties against high resistances. Between these two extremes innumerable
specific requirements must be met. In general, fans of all types in each
general class can be made to perform the same duty, although mechanical
difficulties, noise or lack of efficiency may limit the use to one or another
type. The most common field of service for fans of the propeller type is in
moving air against moderate resistances, especially where no long ducts
or heavy friction must be overcome and where noise is not objectionable,
whereas centrifugal fans are commonly employed for operation at the
comparatively higher pressures and where extreme quietness is necessary,
PERFORMANCE OF FANS
Fans of all types follow certain laws of performance which are useful in
determining the effect of changes in the conditions of operation. These
281
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
laws apply to installations comprising any type of fan, any given piping
system and constant air density, and are as follows:
1. The air capacity varies directly as the fan speed.
2. The pressure (static, velocity, and total) varies as the square of the fan speed.
3. The power demand varies as the cube of the fan speed.
Example 1. A certain fan delivers 12,000 cfm at a static pressure of 1 in. of water
when operating at a speed of 400 rpm and requires an input of 4 hp. If in the same
installation 15,000 cfm are desired, what will be the speed, static pressure, and power?
Speed = 400 X j » 500 rpm
/ ^oox 2
Static pressure = 1 X f TTJA ) — 1-56 in.
Power = 4 X (g?)* = 7.81 hp
When the density of the air varies the following laws apply :
4. At constant speed and capacity the pressure and power vary directly as the
density.
Example 2. A certain fan delivers 12,000 cfm at 70 F and normal barometric pressure
(density 0.07495 Ib per cubic foot) at a static pressure of 1 in. of water when operating at
400 rpm, and requires 4 hp. If the air temperature is increased to 200 F (density 0.06018
Ib) and the speed of the fan remains the same, what will be the static pressure and
power?
Static pressure = 1 X 0*07495 ~ 0-80 in-
5. At constant pressure the speed, capacity and power vary inversely as the square
root of the density.
Example 3. If the speed of the fan of Example 2 is increased so as to produce a static
pressure of 1 in. of water at the 200 F temperature, what will be the speed, capacity,
and power?
Capacity - 12,000 X -_ = 13,392 cfm (measured at 200 F)
0.06018
6. For a constant weight of air:
(a) The speed, capacity, and pressure vary inversely as the density.
(b) The horsepower varies inversely as the square of the density.
Example 4- If the speed of the fan of the previous examples is increased so as to
deliver the same weight of air at 200 F as at 70 F, what will be the speed, capacity,
static pressure, and power?
Capacity = 12,000 X = 14M5 cfm (measured at 200 F)
282
CHAPTER 17 — FANS AND MOTIVE POWER
Static pressure = 1 X -n'f^rr-t~^ ~ 1-25 in.
U.UoULS
FAN EFFICIENCY
The efficiency of a fan may be defined as the ratio of the power required
in moving the air to the power input to the fan. The work done in
moving the air may be computed on the basis of either the static or the
total pressure. When the static pressure is used in the computation it is
assumed that this represents the useful pressure and that the velocity
pressure is lost in the piping system and in the air which leaves the system.
Since in most installations a higher velocity exists at the fan outlet than
at the point of delivery" into the atmosphere, some of the velocity pressure
at the fan outlet may be utilized by conversion to static pressure within
the system, but owing to the uncertainty of friction losses which occur at
the places where changes in velocity take place, the amount of velocity
pressure which is actually utilized is seldom known, and the static pressure
alone may best represent the useful pressure.
The efficiency based upon static pressure is known as the static efficiency
and may be expressed as follows:
St t* ffi * i = cfm X static pressure in inches of water .
lency 6369 X power input expressed in units of 746 watts ( '
Different fans may develop the same capacity against the same static
pressure and with the same power input, and therefore operate at the
same static efficiency, while maintaining different outlet velocities. Where
a high outlet velocity is desirable or can be utilized effectively, the static
efficiency fails to be a satisfactory measurement of the performance. In
many applications of propeller fans, air is circulated without encountering
resistance and no static pressure is developed. The static efficiency is
zero and its calculation is meaningless. Because of such situations where
the static efficiency fails to indicate the true performance, many engineers
prefer to base the calculation of efficiency upon the total or dynamic
pressure. This efficiency is variously known as the total, dynamic, or
mechanical efficiency, and may be expressed as follows:
T t I ffi * — cfm X total pressure in inches of water >«.
iotal efficiency - 6359 x ^^^ input expressed In units of 746 watts ( '
CHARACTERISTIC CURVES
In the operation of a fan at a fixed speed the static and total efficiencies
vary with any change in the resistance which is imposed. With different
designs the peak of efficiency occurs when the fans deliver different per-
centages of their wide-open capacity. Variations in efficiency accompany
variations in pressures and power consumption which are characteristic of
the individual designs and which are influenced particularly by the shape
1See Standard Test Code for Disc and Propeller Fans, Centrifugal Fans and Blowers, Edition of
1932.
283
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
and angularity of the blades. Such variations in pressure, power, and
efficiency are shown by characteristic curves.
Characteristic curves of fans are determined by tests performed in
accordance with the Standard Test Code for Disc and Propeller Fans,
Centrifugal Fans and Blowers2 as adopted by the AMERICAN SOCIETY OF
HEATING AND VENTILATING ENGINEERS and the National Association of
Fan Manufacturers. The results of tests are plotted in different ways : the
abscissae may be the ratio of delivery, assuming full open discharge as
100 per cent, and the ordinates may be static pressure, dynamic pressure,
horsepower and efficiency. Pressures may be expressed in per cent of the
maximum pressure in the manner shown in the illustrations in this
40 50 60
Per Cent of Wide Open Volume
FIG. 1. OPERATING CHARACTERISTICS OF AN AXIAL FLOW FAN
chapter, but in engineering calculations they are sometimes expressed in
proportion to the pressures due to the peripheral velocity.
It should be noted that characteristic curves of fan performance are
plotted for a constant speed. Some variation in values of efficiency may
occur at different speeds but such variation is usually slight within a wide
range of speeds. Fans of similar design but of different size will also show
some difference in efficiency. The proportions of the housing also affect
the performance. As a rule a narrow fan of large diameter shows a higher
efficiency than one of greater width and smaller diameter. For a number
of designs using blades of certain shapes the proportion of the width to the
diameter is so definitely established by the service for which the fan is
intended that little variation in efficiency occurs, but in other designs,
particularly that which uses straight radial blades, the efficiency may
vary over a wide range depending on whether the dimensions are suitable
for a fan intended for ordinary ventilating purposes or for a pressure
blower. Figs. 1 to 4 show characteristic curves for different types of fans
*A.S.H.V.E. TRANSACTIONS, Vol. 29, 1923. Amended June, 1931.
284
CHAPTER 17 — FANS AND MOTIVE POWER
using blades of various shapes, but without reference to the design of
housing employed. The efficiency curves are therefore not serviceable
for making rigid comparisons of efficiencies obtainable with blades of the
various shapes but are intended merely to show reasonable values and
more particularly to show the manner in which variations occur with
changes in fan capacity.
Axial flow fan characteristics are indicated by Figs. 1 and 2. These
fans, when properly designed, have a satisfactory7 efficiency at low
resistance, comparing favorably in this respect with centrifugal fans.
They are low in cost and economical in operation and occupy relatively
little space. Although this type of fan can operate against considerable
30 40 50 60 70
Per Cent of Wide Open Volume
90
FIG. 2. OPERATING CHARACTERISTICS OF AN AIRPLANE PROPELLER FAN
resistance, the noise^ often becomes objectionable, so that it does not
always compare favorably with centrifugal fans for such service. With
most of the designs which employ blades of uniform thickness the power
increases rapidly with an increase in resistance.
The curves (Fig. 1) show the rapid reduction in capacity and increase in
power as the resistance increases. The low efficiency when overcoming
heavy resistance is due to the low speed of the blades near the hub as
compared to the relatively high peripheral or tip speed. The air driven by
the blade area near the rim can pass back through the less effective blade
area at the hub more easily than it can overcome the duct resistance.
Fig. 2 shows the performance of the airplane propeller fan in which the
blades are similar in shape to those of an airplane propeller but of varying
number according to the pressure to be developed. This fan usually
operates at a higher speed than does the former type of propeller fan, and
with a different power characteristic, the power remaining fairly constant
throughout the range of pressures, being somewhat less at the higher than
at the lower pressures. The flatness of the pressure curve indicates the
advantage of this type of fan in preventing overloading of motors where
fluctuations in pressure occur. Variations in the diameter, width, pitch,
285
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
camber, and the thickness of the blades provide a considerable degree of
flexibility in design, so that the peak of total efficiency may be made to
occur at wide-open volume or at various percentages of that volume.
Another advantage of this type of axial flow fan is its low resistance to
air passage when standing still. There are some installations in which
such a characteristic is desirable.
The straight blade (paddle-wheel) or partially backward curved blade
type of fan is practically obsolete for ventilation. Its use is largely con-
fined to such applications as conveyors for material, or for gases con-
taining foreign material, fumes and vapors. The open construction and
the few large flat blades of these wheels render them resistant to corrosion
and tend to prevent material from collecting on the blades. This type of
fan has a good efficiency, but the power steadily increases as the static
Slio
40 50 60 70
Per Cent of Wide Open Volume
80
90
100
FIG. 3. OPERATING CHARACTERISTICS OF A FAN WITH BLADES CURVED FORWARD
pressure falls off , which requires that the motor be selected with a moder-
ate reserve in power to take care of possible error in calculation of duct
resistance.
The forward curved multiblade fan is the type most commonly used in
heating and ventilating work, as it has a low peripheral speed, a large
capacity, and is quiet in operation. The point of maximum efficiency for
this fan occurs near the point of maximum static pressure. The static
pressure drops consistently from the point of maximum efficiency to full
open operation. Fig. 3 shows that this type of fan will have both a high
and a low delivery for a given static pressure at constant speed. The
power curve rises continually from low to peak capacity, but if reasonable
care is exercised in figuring resistance there is no danger of overloading
the motor.
The outstanding characteristics of the full backward curve multiblade
type fan are the steep pressure curves, the non-overloading power curve,
and the high speed. (See Fig. 4.) This fan operates at a peripheral speed
of approximately 250 per cent of the forward curve multiblade type for
286
CHAPTER 17 — FANS AND MOTIVE POWER
like results. The pressure curves begin to drop at very low capacity and
continue to fall rapidly to full outlet opening. The steep pressure curves
tend to produce constant capacity under changing pressures. Where
wide fluctuations in demand occur, this type of fan is desirable to prevent
overloading of motors. The maximum power requirement occurs at
about the maximum efficiency. Consequently a motor selected to carry
the load at this point will be of sufficient capacity to drive the fan over its
full range of capacities at a given speed. The high speed of this type
makes it adaptable for direct connected electric motor drives. The high
speed may necessitate somewhat heavier construction and more operating
attention or service. The dimensional bulk for a given duty often is
150 per cent of that of a forward curve multiblade type fan.
Between the extremes of the forward and the full backward curve blade
type centrifugal fans a number of modified designs exist, differing in the
20 30 40 50 60
Per Cent of Wde Open Volume
FIG. 4. OPERATING CHARACTERISTICS OF A FAN WITH BLADES CURVED BACKWARD
angularity or in the shape of the blades. Common among these designs
are the straight radial blade type, the radial tip type, and the double
curve blade type with a forward angle at the heel and a slight backward
angle at the tip of the blade. Characteristic curves of these types show
varying degrees of resemblance to the curves of Figs. 3 and 4, according
to the degree of similarity to one or the other of the two designs of fan
considered.
SELECTION OF FANS
The following information is required to select the proper type of fan ;
1. Cubic feet of air per minute to be moved.
2. Static pressure required to move the air through the system.
3. Type of motive power available.
4. Whether fans are to operate singly or in parallel on any one duct.
& What degree of noise is permissible.
6» Nature of the load, such as variable air quantities or pressures.
287
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Knowing the requirements of the system, the main points to be con-
sidered for fan selection are (1) efficiency, (2) speed, (3) noise, (4) size and
weight, and (5) cost.
In order to facilitate the choice of apparatus, the various fan manu-
facturers supply fan tables or curves which usually show the following
factors for each size of fan operating against a wide range of static
pressures:
1. Volume of air in cubic feet per minute (68 F, 50 per cent relative humidity,
0.07488 Ib per cubic foot).
2. Outlet velocity.
3. Revolutions per minute.
4. Brake power.
5. Tip or peripheral speed.
6. Static pressure.
The most efficient operating point of the fan is usually shown by either
bold-face or italicized figures in the capacity tables.
Fans for Ventilation and for Cooling Systems
Two important factors in selecting fans for ventilating systems are
efficiency (which affects the cost of operation) and noise. First cost and
space available are secondary. The fans should be selected to operate
at maximum efficiency without noise. Because noise in a ventilating
system is irritating and a cause for complaint, fans must be selected of
proper size in order to reduce it to a minimum. Noise may be caused by
other factors than the fan, namely, high velocity in the duct work,
unsatisfactory location of the fan room, improper construction of floors
and walls, and poor installation. Where noise is chargeable directly to
the fan, it is caused either by excessive peripheral speeds, or the fan is of
insufficient size. It should be remembered, however, that the tip speed
required for a specified capacity and pressure varies with the type of
blade, and that a tip speed which may be excessive for the forward
curved type is not necessarily so for the backward or slightly backward
type. A noisy fan usually is one which is operated at a point considerably
beyond maximum efficiency.
For a given static pressure there is a corresponding outlet velocity and
peripheral speed wherein maximum efficiency is obtained. If a fan is
selected to operate at this point, the cost of operation and the noise can
be held within control.
To aid in selecting fans as near as possible to the point of maximum
efficiency, there are listed in Tables 1 and 2 for each static pressure cor-
responding outlet velocities and tip speeds which will give satisfactory
results. The proper tip speed for a given static pressure varies with the
design of wheel and with the number of blades or vanes in the wheel.
Lower outlet velocities than those listed in Table 1 may be employed,
but care must be exercised when fans of the forward curved type are used
to avoid selecting a fan for operation below its useful range. The useful
range of the fans of Table 2 extends over the full length of the per-
formance curve.
In exhaust ventilating systems where the air column moves toward the
288
CHAPTER 17 — FANS AND MOTIVE POWER
fan, noise due to the higher tip speeds and outlet velocities will not be
so readily transmitted back through the air column to the building as
when the air column is moving toward the rooms. Therefore higher
outlet velocities may be used, but this will be at the expense of increased
horsepower.
Amply large fans should always be used for both exhaust and supply
systems, as there may be and usually is leakage despite the most careful
workmanship, necessitating the delivery of more air at the fans than is
exhausted from or supplied through the openings in the various rooms.
Long runs of distributing ducts, heaters, and air washers require
definite increments of the total pressure which a supply fan in a venti-
lating system must overcome. These static pressures should be con-
sidered when selecting the fan characteristics, speed, and power.
TABLE 1.
GOOD OPERATING VELOCITIES AND TIP SPEEDS FOR FORWARD CURVED
MULTIBLADE VENTILATING FANS
STATIC PRESSURE
OUTLET VELOCITY
TIP SPEED
INCHES OP WATER
FEET PEE MINUTE
FEET PER MINUTE
M
1000-1100
1520-1700
% looo-iioo
1760-1900
H 1000-1200
1970-2150
&
1100-1300
2225-2450
1200-1400
2480-2700
%
1300-1600
2660-2910
1
1500-1800
2820-3120
JLM
1600-1900
3162-3450
1J^
1800-2100
3480-3810
1H
1900-2200
3760-4205
2
2000-2400
4000-4500
2M
2200-2600
4250-4740
2H
2300-2600
4475-4970
3
2500-2800
4900-5365
Fans picked within the limits of Table 1 will operate close to the point
of maximum efficiency. No attempt has been made to select these limits
for quiet operation, since this is a relative term and varies with the type
and location of the installation.
The connection of a fan to a metallic duct system should be made by
canvas or a similar flexible material so as to prevent the transmission of
fan vibration or noises. Where noise prevention is a factor the fan and its
driver should have floating foundations.
Fans for Drying
Both axial flow and centrifugal types of fans are used for drying work.
Propeller fans are well adapted to the removal of moisture-laden air when
operating against low resistance and when handling air at low tempera-
tures. Motors on these fans usually are of the fully-enclosed moisture-
proof types so that saturated air or air containing foreign material will
not injure the motors.
Unit heaters employing axial flow fans are widely used in the drying
field. In drying, these fans may be used with unit heaters where not
too much duct work is required and where air is to be delivered against
289
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
pressure, since the noise developed from the high peripheral speed of these
fans is not ordinarily objectionable in process work.
Centrifugal fans of the multiblade type generally are selected to supply
air for drying, as they are capable of delivering large volumes of air
against all pressures likely to be encountered.
Belt driver! fans usually are to be preferred to direct-connected fans
since efficient motor speeds do not usually coincide with efficient fan
speeds. Replacement of a standard motor is quick and easy if it is belted.
Wherever drying is done throughout the year and where air require-
ments change as the drying conditions change, the drying can be speeded
up or reduced through control of the fan capacity. This may be done by
changing the fan speed or by varying the outlet area with dampers. A
throttled outlet reduces the volume and reduces the power.
Due to the low speeds of forward curved multiblade or paddle-wheel
type fans, these can be direct-connected to reciprocating steam engines,
TABLE 2. GOOD OPERATING VELOCITIES AND TIP SPEEDS FOR MULTIBLADE VENTILATING
FANS WITH BACKWARD TIPPED AND DOUBLE CURVED BLADES
STATIC PRESSURE
INCHES of WATER
OUTLET VELOCITY
FEET PER MINUTE
TIP SPEED
FEET PER MINUTE
H
800-1100
2600-3100
B/S
800-1150
3000-3500
jl
900-1300
3400-4000
H
1000-1500
3800-4500
%
1100-1650
4200-5000
%
1200-1750
4500-5300
1 : 1200-1900
4800-5750
1M
1300-2100
5300-6350
1H
1400-2300
5750-6950
iH
1500-2500
6200-7550
2
1600-2700
6650-8050
2J4
1700-2800
7050-8550
2H
1800-2950
7450-9000
3
2000-3200
, 8200-9850
ctnd the exhaust steam from the engines may be used in the heating
apparatus. In selecting engine driven fans for drying processes, where a
large quantity of exhaust steam is used in the heaters r a smaller fan and
greater power consumption may be used, because power economy is not
essential under this condition.
Where static pressure in a dryer varies, and where several fans must
operate in parallel, fans are to be preferred which have a continuously
rising pressure characteristic, such as is given by backward-curved or
double-curved blades. This type of fan is well adapted for direct-con-
nected motors of the higher speeds.
Fans far Dust Collecting and Conveying
The application of fans for handling refuse, dust, and fumes generated
by machine equipment is covered in Chapter 21. Information is given
regarding the methods for determining air quantities, the velocity required
for carrying various materials and the method of determining maintained
290
CHAPTER 17 — FANS AND MOTIVE POWER
resistance or total static pressure at which the fan is to operate. The
selection of a proper size fan is at times governed by the future require-
ments of the plant. In many instances, additional future capacity is
anticipated and should be provided for.
Having determined the necessary volume of air and the maintained
resistance or static pressure required, the proper size fan may be selected
from the fan manufacturers' performance charts or capacity tables. The
fan chosen should be the size that will provide the required ultimate
quantities with the minimum power consumption.
FAN CONTROL
Some method of volume control of fans usually is desirable. This may
be done by varying the peripheral velocity or by interposing resistance, as
by throttling-dampers. Both methods, since they reduce the volume of
air, reduce the power required. In many installations adjustments of
volume are desirable during varying hours of the day. In others an
increased supply of air in summer over that needed for winter is demanded.
Experience is required in deciding whether speed-control or damper-
control shall be used for specific cases. Where noise is a factor, it may be
exceedingly desirable to reduce the speed at times, while on the other
hand, any fan which has its normal speed reduced as much as 50 per cent
without change in resistance will move only 50 per cent of the air.
DESIGNATION OF FANS
Facing the driving side of the fan, blower, or blast wheel, if the proper direction of
rotation is clockwise, the fan, blower, or blast wheel will be designated as clockwise.
If the proper direction of rotation is counter-clockwise, the designation will be counter-
clockwise. (The driving side of a single inlet fan i& considered to be the side opposite
the inlet regardless of tie actual location of the drive.)8
This method of designation will apply to all centrifugal fans, single or double width,
and single or double inlet. Do not use the word "hand," but specify ''clockwise" or
* ' counter-clockwise."
The discharge of a fan will be determined by the direction of the line of air discharge
and its relation to the fan shaft, as follows:
Bottom Tiorizontal: If the line of air discharge is horizontal and below the shaft.
Top horizontal: If the line of air discharge is horizontal and above the shaft.
Up blast: If the line of air discharge is vertically up.
Down blast: If the line of air discharge is vertically down.
All intermediate discharges will be indicated as angular discharge as follows:
Either top or bottom angular up discharge or top or bottom angular down discharge,
the smallest angle made by the line of air discharge with the horizontal being specified.
In order to prevent misunderstandings, which cause delays and losses,
the arrangements of fan drives adopted by the National Association of
Fan Manufacturers and indicated in Fig. 5 are suggested.
If double width, double inlet fans are selected, care must be taken that
both inlets have the same free area. If one inlet of a forward -curved Made
type of fan is obstructed more than the o|her, the fan -will not operate
properly, as one half of the^tgel^ill delivet more air than the other half.
,
^Recommendations adopted by the National Association of "Fan Manufacturers.
291
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
a
§ c
*l
Arr. 4*
For direct drive.
overhung. No bearii
mounted on motor
Pedestal for motor
-" \
n\=i
3 a §•
Its
Similar
on fan,
couplinj
&
o
9
w
i
P3
04
<
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2*
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292
CHAPTER 17 — FANS AND MOTIVE POWER
The backward curved and double curbed types with backward tip operate
satisfactorily in double or in parallel operation.
MOTIVE POWER
It is no easy matter to predetermine the exact resistance to be encoun-
tered by a fan or, having determined this resistance, to insure that no
changes in construction or operation shall ensue which may increase air
resistance, thus requiring more fan speed and power to deliver the required
volume, or which may reduce air resistance, thus causing delivery of more
air and a consequent increase of power even at constant speed.
It is recommended, therefore, for centrifugal type fans that the rated
power to be supplied shall exceed the rated fan power by a liberal margin ,
when forward cawed types are used. When backward or double curved
blade types are used, motors with ratings very close to that of the fan
horsepower demand can be employed.
Justification for liberal power provision exists also in the possibility
of varying demand due to changes in ventilation requirements, intensity
of occupation, and weather conditions.
The motive power of fans should be determined in accordance with the
Standard Test Code for Disc and Propeller Fans, Centrifugal Fans and
Blowers, as adopted by the AMERICAN SOCIETY OF HEATING AND VENTI-
LATING ENGINEERS and the National Association of Fan Manufacturers.
Fans may be driven by electric motors, steam engines (either horizontal
or vertical), gasoline or oil engines, and turbines, but as previously stated
the drive commonly used is the electric motor.
ELECTRIC POWER
Each typje of electric motor and kind of electric current has its advan-
tages and disadvantages as applied to a fan. For motor specifications and
standards, the Motor and Generator Standards of the National Electrical
Manufacturers Association should be consulted.
Direct-connected electric motors usually are very efficient for fan
driving because there is no slippage due to belts, and no wear or noise due
to chains or gears. There is less maintenance and upkeep to a direct-
connected unit, and with an overhung fan wheel on the motor shaft, the
usual fan bearings are eliminated.
The disadvantage of a slow-speed direct-connected motor is that it
may be unduly large and heavy as well as costly, but this may be offset
by the compactness of the unit as a whole due to limited space for fan
equipment.
Should anything go wrong with a slow-speed direct-connected motor
there may be a considerable delay in securing replacements, as these
motors are not usually carried in stock, as is the case with moderately
high-speed motors.
If a change of speed is found necessary with a direct-connected motor,
it will mean a change of motor, which may necessitate a change in the
motor foundation usually built with the fan in such cases. On* the other
hand, non-direct-connected motors have transmissions subject to wear
and slippage, and chains or gears may be noisy with this latter type.
293
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 3. CLASSIFICATION OF MOTORS
GBOUP
SUB-
DIT.
TYPE
CUR-
RENT
SPEED
CHAR-
STARTING
TORQUE
STARTING
CURRENT
APPLICATIONS
ACTERISTICS
A
1
Shunt wound
d-c
Constant
Medium
High
Fans
2
Squirrel-cage
a-c
Constant
Medium
High — about
Fans, centrifu-
six times full
gal pumps
load
3
Synchronous
a-c
Constant
Medium
Starts as squir-
rel cage motor
Motor genera-
tor sets, air
compressors,
fans
4
Slip ring or
a-c
Constant
Heavy
Low
Vacuum pumps,
wound rotor
air compres-
sors
5
Double squir-
a-c
Constant
Heavy
Medium
Frequent and
rel-cage
heavy starting
loads, pumps,
compressors
6
Low-torque
a-c
Constant
Light
Low
Direct-con-
capacitor
nected fans
7
High-torque
a-c
Constant
Medium
Low
Belt drive of
capacitor
fans
8
High -torque
a-c
Constant
High
Medium
For heavy
capacitor
starting load
such as larger
fans, pumps,
compressors
9
Repulsion-
a-c
Constant
High
Medium
Fans, pumps,
induction
compressors
B
1
Brush shifting
a-c
Adjustable
Medium
Low
Stokers, boiler
fans
2
Cumulative
d-c
Adjustable
Heavy
• High
Pumps
comp'd with
shunt
predominance
3
Squirrel -cage,
poles can be
a-c
Multi-
speed
Medium
High
Fans, ice ma-
chines
regrouped
C
1
Series
d-c
Variable
Heavy
Low
Fans
2
Cumulative
d-c
Variable
Heavy
Low
Single-acting
comp'd with
reciprocating
series
pumps
predominance
3
Slip ring —
a-c
Variable
Heavy
Low
Fans
using external
resistance in
' secondary
294
CHAPTER 17 — FANS AND MOTIVE POWER
However, should a change in speed be necessary where the motor is not
direct-connected, changes in speed ratio can easily be accomplished by
changing pulleys, sprockets or gears on either the fan or the motor. In
the case of a motor breakdown a standard stock motor may easily be
substituted.
A type of drive using a wedge-shaped rope-like belt, singly or in multi-
ple, and capable of use on short pulley-centers is very popular, as it
enables the use of high speed motors with slow speed fans. The com-
pactness secured by this equipment compares favorably with that of a
direct connected layout. This type of drive also is very quiet in operation,
being similar to a conventional belt drive in this respect. Alternating
current motor designs are such that improved operating characteristics
are obtained with the higher motor speeds. Efficiencies and power
factors are improved over those in effect with slower speed motors, thus
showing a considerable saving in power consumption, and militating in
favor of some effective speed-reducing transmission device such as is
given by multiple wedge-shaped belts.
Quietness of operation is more readily obtained with moderately high
speed induction motors than with low speed motors, as any slight magnetic
unbalance in the latter is not as easily heard. Amplifications of motor
induction noises in parts of a building remote from the motor equipment
sometimes are carried by the steel work, ducts, or piping in the building.
There is considerable evidence that these sounds are more easily con-
trolled with high motor speeds than with low ones.
Motors which are practically quiet in operation and free from magnetic
disturbing noises can be obtained, and should always be specified for
quietness of operation when used for fan installations in buildings where
quietness is a factor.
In the construction of fan and motor foundations where the machinery
is mounted on the floor or upon a concrete platform, it is a usual practice
to install a layer of cork on top of which is laid or floated the base which
carries the apparatus. It is essential that the bolts or lag screws which
fasten the machines to this foundation shall not extend through to the
floor. It is wise to fasten curbs to the floor, these presenting insulated
surfaces to the machinery foundation and so preventing it from traveling.
Rubber, especially in shear or in tension, is valuable as a sound absorber
in foundations for machinery. Steel shoes for fans and motors with
rubber inserts are available. Steel springs are also used effectively for
this purpose.
The general classification of motors used for heating, ventilation and
air conditioning is shown in Table 3.
Control for Electric Motors
Very small direct current motors may be started by throwing them
directly on the line through a suitable starting switch. The larger sizes
require some type of starting rheostat. When speed adjustment is
desired, the controller for adjusting the speeds of the motor usually
functions also as a starting device.
Alternating current motors of 5 hp and under usually may be thrown
directly on the line. It is good practice to use a starting switch equipped
285
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
with a thermal overload or inverse time limit overload device. This type
of switch provides protection to the motor beyond that given by fuses.
Fuses, when used, necessarily must be large enough to take care of the
inrush current but this makes them inadequate for protecting the motor
under operating conditions. The thermal overload device allows for this
inrush and does not function until an overload has become persistent, the
time element depending upon the percentage of overload beyond the
rating of the element. This type of switch is available for manual opera-
tion and also is furnished in the magnetic type for remote operation by
push button, or for operation by other types of pilots, such as pressure
switches and thermostats.
On standard squirrel cage motors above 5 hp a starting compensator
usually is employed to keep the inrush current within the limits specified
by the local power companies. Compensators may be obtained in trans-
former types and primary resistor types, and usually are furnished for
manual operation. They can be secured for remote control also, but
necessarily are expensive. However, the new type of high reactance, self-
starting motors usually may be thrown across the line up to 30 hp in size,
and still have their inrush current within the limits of the rules of the
National Electric Light Association. With this type of motor a magnetic
contactor usually is used. This device may be operated from a remote
point by push button, if desired. These magnetic contactors are furnished
usually with thermal overload and no-voltage protection.
For remote operation of motors through magnetic starters, the operat-
ing buttons may be located in the engineer's or manager's office, and
tell-tale indicating lamps may be wired up with the circuit to indicate
whether or not the unit is in operation. This type of control is very
desirable in large buildings where the engineer is to .have complete charge
of the ventilating system.
Remote or automatic control of the units may be effected also by
pneumatic or hydraulic apparatus, or by thermostats or by pressure
devices which are provided with electric contacts for starting or stopping
the units upon reaching certain conditions.
Variable speed slip ring motors and direct current motors may also
be arranged for remote speed control by means of pre-set automatic
regulators, where the operating speed of the motor is set by a dial-switch
(which may be near the fan or at a remote point) and the motor is then
automatically controlled at any given speed merely by operating the
remote control push button for starting or stopping the equipment.
Arrangements may be made for remote control of fan motors, or for
automatic control by influence of temperature. Remote control may be
by pneumatic or by hydraulic manipulation as well as by electrical means.
In many large ventilating systems which have heating plants in con-
nection, steam engines are used to operate fans. A medium speed steam
engine, exhausting at low pressure into the heating system is a very
economical source of power, is quiet in operation, and has a wide range of
speed variation. The steam, economy of such an engine usually is of little
importance, since the engine serves as an auxiliary to the pressure-
reducing valve interposed in such cases between the boiler and the heaters.
Internal combustion engines and line shafting often are used for fan
296
CHAPTER 17 — FANS AND MOTIVE POWER
driving, requiring clutches or shift-belts with loose pulleys in order to
secure proper starting and control.
Ability to adjust the speed of ventilating fans is desirable as a measure
of economy and adaptability to varying loads, but where such adjust-
ments are provided very definite speed and pressure indications should be
supplied at the controller, since without them in most cases the operator
would be compelled to guess at the output.
REFERENCES
Heating, Ventilating and Air Conditioning, by Harding and Willard, Revised Edition,
1932.
Fan Engineering, Buffalo Forge Company.
Theories and Practices of Centrifugal Ventilating Machines, by D. Murgue, trans-
lated by A. L. Stevenson.
Mechanical Engineers' Handbook, by Kent.
Mechanical Engineers' Handbook, by Lionel S. Marks.
Constructive Mechanism and the Centrifugal Fan, by George D. Beals.
Coal Miners Pocket Book.
The Fan, by Charles H. Innes.
Mine Ventilation, by J. J. Walsh (A.S.H.V.E. TRANSACTIONS, Vol. 23, 1917).
Fan Blower Design, by H. F. Hagen (A.S.H.V.E. TRANSACTIONS, Vol. 28, 1922).
The Centrifugal Fan, by Frank L. Busey.
Section X, A.S.H.V.E. Code of Minimum Requirements for the Heating and Venti-
lation of Buildings (Edition of 1929).
PROBLEMS IN PRACTICE
1 • In a public building, what type of fan is suitable for:
a. A supply fan?
b. An exbaust fan?
a. The centrifugal housed fan is well suited for this work. The various types are the
forward curved blade, the radial blade, the full backward curved blade, and the medium
speed double curved blade with backward tip. When direct connected motors are to be
used, the backward tip fans, on account of their speeds, are better adapted. This type
has the added advantage of having a limiting horsepower characteristic which will
prevent an overload on the motor. Where the belt drive is used, all of the above types
are suitable.
b. For exhaust work all of the above types, as well as disc and propeller fans are suitable,
although the latter are seldom used except where there is little or no duct work con-
nected to the fan.
2 • In selecting fans for quiet operation in public buildings :
a. Should the outlet velocity of the fan be limited?
b. Should the tip speed of the fan be limited?
a. Because all commercial fans operating at pressures suitable for this class of work
would be considered noisy if the fan were to discharge directly into the room, and
because the duct system on the fan discharge is depended upon to absorb a reasonable
amount of fan noise, it is desirable to have a moderate run of duct work with some bends
and elbows included as sound deadeners. Where this duct is of necessity very short, the
outlet velocity must be kept down to the lower limits recommended in this chapter or
else an efficient sound absorber must be used. The experience of the engineer must be
his guide in determining the allowable outlet velocity in each individual case.
b. Tip speed should not ordinarily be limited, because different types of fan blades have
entirely different allowable tip speeds for quiet operation. A fan having a backward
blade at the tip can run at much higher tip speed than can a forward curved or a straight
blade fan, with the same degree of quietness.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
3 • Is a direct connected or a belted fan preferable in public building work?
Where space is at a premium, direct connection is best. Next in space economy is the
short V-belt drive. The flat belt drive fan requires the greatest floor space. In this
class of work, pressures are usually so low that even with the high speed fans the motor
cost is greater for direct connected units than for belt drive fans.
4 • a. What type fans are used in industrial work?
b. What outlet velocity is suitable?
a. All of the centrifugal types are suitable; the disc and propeller types are suitable for
low pressure work, or they are often used as exhausters.
b. The outlet velocities on fans for industrial work can be much higher than can those in
public building work, where quietness is essential. Fans should be selected with outlet
velocities as recommended in this chapter, using the upper limit of velocities.
5 • Are direct connected or belted fans preferred in industrial work?
In industrial applications, fans are often advantageously direct connected to motors.
The pressures are usually high enough to use standard motor speeds. The high speed
types of fans have limiting horsepower characteristics so that little margin in power must
be provided in the driving motor. Belted fans may be used, but where high power is
required a special arrangement is often necessary for shaft and bearings on account of the
weight of the sheave and the belt pull.
o • A forward curved multiblade fan which requires 5.4 bhp is delivering 22,800
cfm at 70 F against a resistance pressure of 1 in. of water at an outlet velocity
of 1440 fpm:
a. What is the static efficiency?
b. What is the total efficiency?
a. 66.3 per cent (see Equation 1).
b. 74.5 per cent (see Equation 2).
7 • If the above fan has a 54-in. diameter wheel and operates at 193 rpm,
will it be suitable for a ventilating installation where a minimum of noise is
desirable?
Yes. The tip speed will be 2720 fpm and this, together with the 1440 fpm outlet velocity,
falls within the limits given in Table 1 for 1-in. resistance pressure.
8 • Assuming that a 7^4 hp constant speed, high reactance type, self -starting
electric motor is used to drive the above fan, what electrical starting apparatus
should be used for control from a remote point?
An across-the-Kne type magnetic push button starter with indicating lamps to show
whether or not the unit is in operation.
9 • What objectionable feature is inherent in the ordinary propeller fan when
it is operating at high resistance pressures?
It must operate at a high speed with consequent noise.
10 • At what point should a fan be selected for operation, and why?
At its point of maximum efficiency because the cost of operation and the noise produced
will be least.
298
Chapter 18
SOUND CONTROL
Measurement of Noise, Noise in Buildings, Coefficients of
Absorption, Insulation of Air-Borne Sound, Location and
Insulation of Equipment Room, Insulation of Machinery and
Solid-Borne Vibration, Control of Noise Transmission Through
Ducts, Effect of Humidity upon Acoustics
THE ventilating and air conditioning of any space affect its acoustics
and become apparent when consideration is given to the require-
ments for good hearing in any architectural interior. The requirements
which must be given careful study are:
1. The room, should be free from noise, whether of inside or outside origin.
2. The useful sound, whether speech or music, should be sufficiently loud (with
reference to any residual noise) to be heard easily and distinctly.
3. The useful sound should be distributed uniformly in all parts of the room, and the
sound reaching the listeners should be free from long-delayed reflections which produce
interference or echoes.
4. The room should be free from pronounced resonant tones which may result from
either volume or panel resonance.
5. The room should contain sound-absorptive materials in such amounts, and of such
qualities, as will provide a proper balance between the persistence and cessation of the
articulated components of sound, that is, the reverberation in the room should be long
enough to sustain harmony and impart tonal blending to music, and at the same time it
must be short enough to prevent the overlapping and confusing of the separate sounds
of speech.
Obviously, the first of these requirements is the one which imposes
restrictions on the installation of air conditioning or ventilating equip-
ment— the equipment noises must be unobjectionable in occupied rooms —
although the fifth requirement is not entirely independent of the humidity
and temperature of the air.
LOUDNESS
Loudness is the sensation of sound intensity. When it is said that one
sound is louder than another a difference in intensity level is implied.
Two identical whistles when sounded together do not make a sound twice
as loud as one. It may take ten to make a sound 20 per cent louder than
one* It has been found that loudness bears a logarithmic relationship to
intensity of sound. On this basis a scale of loudness has been built and a
unit, the decibel (db), has been established. This scale is illustrated in
Fig. 1 which shows the loudness of some typical noises. The formula for
relating loudness and intensity is:
Xi - L* - 10 log* A (1)
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
where
L = Loudness in db; / = Intensity.
Thus the two whistles made a noise 10 logic 2 = 3 db louder than one
whistle and the ten whistles, 10 logic 10 = 10 db louder than one. It
would take a hundred whistles to make a noise 20 db louder than one and
a thousand to make a noise 30 db louder.
MEASUREMENT OF NOISE
Since the chief acoustical problem in the ventilating or air conditioning
of a building consists of reducing equipment noise, it is necessary to
describe methods for measuring noise. The measurement of noise is a
relatively new problem, and although there are several reliable methods,
there are as yet no standardized units, scales, or instruments for measuring
noise1. However, the decibel (db) described above is widely used in this
country and England as the standard unit for noise or sound intensity — a
unit of the same size, but called a phon, is used in Germany — and the zero
level of the scale is >a barely audible sound. Since the relation between
subjective loudness and sound intensity is dependent upon pitch, it is
customary to refer loudness to a single frequency. A 1000-cycle tone is
generally accepted as the reference frequency, that is, the loudness of any
sound is rated in terms of an equally loud 1000-cycle tone. Thus, a noise
of 50 db means that the noise would be judged to be of the same loudness
as a 1000-cycle tone which is 50 db above the normal threshold of audi-
bility for the 1000-cycle tone.
As the frequencies decrease below 1000 cycles, the ear becomes less
sensitive, until at about 30 cycles sounds are no longer audible regardless
of their intensity. Similarly, for higher frequencies, the limit of audi-
bility is reached around 7000 cycles. Thus, at frequencies below 1000
cycles, sounds of the same loudness must have a greater intensity than at
1000 cycles. This is particularly fortunate, as otherwise the low fre-
quency sounds would mask all others.
Noise measurements are usually made by one of three methods. The
first is the electrical instrument method, which uses a noise meter usually
consisting of a microphone, an amplifier, and a galvanometer. Where
such a meter is to measure the loudness of a noise without regard to the
frequency distribution, it must contain a weighted network which elec-
trically simulates the varying sensitivity of response of the ear to different
frequencies. Where it is desired to analyze the character of the sound,
filters which shut out all but certain bands of frequencies are used with the
meter. A number of manufacturers make such meters.
The second method consists essentially of varying the intensity of an
artificially generated sound until the noise generated is masked by the
noise being measured. Obviously, this method is subject to human errors
in observation to which the instrumental method is not, but in the hands of
*See Proposed Tentative Standards for Noise Measurement, and Proposed American Tentative Standard
Acoustical Terminology of the American Standards Association Sectional Committee on Acoustical Measure-
ments and Terminology.
Also see How Sound is Controlled, by V. O. Knudsen (Heating, Piping and Air Conditioning, October,
1931), and Acoustical Problems in the Heating and Ventilating of Buildings, by V. O. Knudsen (A.S.H.V.E.
TRANSACTIONS, Vol. 37, 1931).
300
CHAPTER 18 — SOUND CONTROL
a careful observer quite satisfactory results may be obtained. One
instrument used is the audiometer, which consists of a buzzer, an ear
phone, and a rheostat. The phone is held a fixed distance from the ear
while the resistance of the rheostat is varied until the sound of the buzzer,
as transmitted electrically to the phone, can no longer be heard. Audio-
meters are available either for covering all frequencies, as in the noise
meter, or for covering certain frequency bands only.
A third method of measuring noise, simple, yet sufficiently accurate for
most field measurements, employs only three tuning forks and a stop
watch. Forks having frequencies of 128, 512, and 2048 are recommended.
The forks must be calibrated. That is, it is necessary to know for each
fork (1) the initial intensity, in number of decibels above its threshold,
immediately after it has received a standard hit or excitation, and (2) the
damping rate, in decibels per second. These calibrations can be made in
any well-equipped acoustical laboratory. A standard hit or excitation can
be imparted to the fork by a felt-covered spring hammer, or simply by
letting the fork fall from a vertical position through an arc of 90 deg,
hitting a suitable pad (such as soft rubber or felt for the 128 and 512 forks
and hard rubber for the 2048 fork). The average 512 steel fork will have
an initial intensity, when held % in- from the ear with the broad side of
the prong facing the ear canal, of about 80 db, and will decay at a rate of
about 1.0 db per second. Such a fork will remain audible about 80 sec
in a perfectly quiet place, provided the listener has normal hearing. In
the presence of a noise, it will remain audible until its tone is just masked,
by the noise. Thus, if a 512 fork, having an initial intensity of 80 db and
a damping rate of 1.0 db per second, should be found to remain audible
35 sec in the presence of a certain noise, the masking effect of the noise
is 80 - 35, or 45 db.
Procedure
The method of measuring any noise is as follows: The observer, in the
presence of the noise, strikes the 128 fork a standard blow. At the same
instant he starts a stop watch. The fork is then held in front of the ear
canal, and moved back and forth slightly, until the tone of the fof!Ti§~JTist
completely masked by the noise, at which instant the watch is stopped.
This measurement is repeated at least two times. The average time is
subtracted from the time the 128 fork remains audible in a quiet place.
This difference multiplied by the damping rate of the fork gives the mask-
ing effect of the noise at 128 cycles. Similar measurements are made with
the 512 and 2048 forks. Measurements of this type give a satisfactory
description of both the intensity and the frequency distribution of the
noise. The average masking effect of the noise at 128, 512, and 2048
cycles will usually be about 5 to 10 db less than the reading given by a
noise meter.
NOISE IN BUILDINGS
Measurements of the intensity of speech, music and noise in many
buildings, with special consideration of the noise produced by ventilating
equipment, have given the results indicated by Fig. 1. The equivalent
loudness of sounds in buildings varies from less than 10 db near the
outlet of an air duct in a very quiet sound studio to nearly 100 db in a
noisy boiler factory. It will be noted that the noise from the ventilating
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
fan in a certain high school auditorium was nearly as loud as average
speech in a large auditorium. Such an amount of noise is devastating to
good acoustics; in fact, it is impossible to hear speech in the presence of
such a noise.
db
Average Loudness of Music m Room-
Conversation in a Small Room-
Speech m a Small Auditorium -»•
Speech in a Large Auditorium
100
*- Boiler Factory
90
80
*• Ventilating Room for Large Hotel ( Very Noisy )
70
60 -e-
50
40
30
20
10
-Electric Power Substation
-Inside of Duct, near Large Low Speed Fan
-Equipment Room ( Average Condition ;
-Fan Room for School Building ( Rather Quiet )
-Guest Room, Large Hotel on Noisy Street
{ Windows Open )
..Near Outlet of Ventilating Duct m High School
Auditorium (Very Noisy, no "Filters" in Duct)
- Fan Noise in Theater ( Poor Control of Noise )
-Fan Noise in Theater ( Proper Control of Noise)
_Near Outlet of Ventilating Duct in M. G. M
~ Sound Studio ( Planned Control of Noise )
FIG. 1. CHART SHOWING THE EQUIVALENT LOUDNESS (IN DECIBELS) OF SPEECH, Music,
AND A NUMBER OF NOISES INCIDENT TO THE VENTILATING OF ~
•Acoustical Problems in the Heating and Ventilating of Buildings, by V. O. Knudsen (A.S.H V.E
TRANSACTIONS, Vol. 37, 1931).
In every problem of noise reduction in buildings it is necessary to know
how much noise can be tolerated. The noise levels given in Table 1 may
be regarded as completely inoffensive. They represent what might be
termed ideal conditions, not often realized in existing buildings. How-
ever, they represent conditions which can be attained by proper control
of noise, and the heating and ventilating engineer should aim to provide
the degree of quiet specified in the table.
In considering the tolerable room noise level due to heating, ventilating,
or air conditioning apparatus, not only must the absolute value of the
noise be considered but also its relation to the room noise level without
the apparatus running. This is necessary since a large increase of noise
subjects the apparatus to serious criticism even though the level may be
low. It must also be borne in mind that the noise produced by the ap-
302
CHAPTER 18 — SOUND CONTROL
paratus is additive to that of the room without apparatus. Thus if the
two are equal, when combined the noise level will be 3 db higher. For
these reasons the room noise caused by the apparatus should not exceed
the other room noise.
Noise Control
Essential to the design of a satisfactory system are: first, a knowl-
edge of the nature and intensity of the noise generated by the various
parts of the equipment; second, a knowledge of how to vary the noise
level between the apparatus and the conditioned room if need be;
third j a knowledge of the acceptable level of apparatus noise in the con-
ditioned room. Besides these, the engineer must be able to deal with
other noises which might enter the room when openings are made into it,
such as cross talk between rooms connected with common ducts, and noise
TABLE 1. ACCEPTABLE NOISE LEVELS
Talking picture studios ,
Radio broadcasting studios ,
Hospitals _.
Music studios
Apartments, hotels, homes, small private offices
Theaters, churches, auditoriums, classrooms, libraries _
Talking picture theaters, small clothing stores
General offices
Large public offices, banking rooms, upper stories of department
stores, restaurants, barber shops
Grocery stores, drug stores
Accounting and typewriting offices-
Main floor of department stores
6 to 8 db
8 to 10 db
8 to 12 db
10 to 15 db
10 to 20 db
12 to 24 db
15 to 25 db
20 to 30 db
25 to 35 db
30 to 50 db
35 to 45 dD
40 to 50 db
transmitted to portions of duct systems outside the conditioned room and
thence to its interior.
The problem of apparatus noise is receiving the study of equipment
manufacturers who are aiming at both noise reduction and standardiza-
tion. Some manufacturers now have noise ratings available for their
equipment, while some pass each unit of equipment of certain types
through sound tests during the course of manufacture.
The problem of noise reduction from apparatus to room must take into
consideration and treat separately the three modes of travel of noise to the
room : first, from the apparatus through the air to the walls of the room
and thence to its interior; second, through the building structure to the
room; third, through ducts or openings to the room. Because the noise
entering by each of these three channels is susceptible to quantitative
analysis, solutions are available. Along with the transmission of sound
through the building structure, the engineer must also consider the
transmission of vibration, which may also be objectionable. The solution
is not complete, however, until the effect of the noise entering the room on
the, room noise level is determined.
ROOM NOISE LEVEL, COEFFICIENTS OF ABSORPTION
One of the most effective means of reducing noises in ventilating equip-
ment is accomplished by the proper covering of the interior walls and
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
ceiling of the equipment room, or the inner walls of the ducts, with sound-
absorptive materials. The intensity / of a continuous sound in a room is
E PS*
I = or --— 2
a a
where
E — the rate of emission of the noise source = I1 5'. (The intensities of noises entering
the room times the areas through which they enter.)
a = the total amount of absorption supplied by the boundaries and contents of the
room.
= otiSi + <x«Sz + a353 -f , wJiere Si, 52, 58f are the areas of the
boundary materials for the room, and «i, a>, «3, are the corresponding coefficients
of absorption.
Hence, by increasing tenfold the absorptivity of the boundaries of a room it is possible
to reduce tenfold the average intensity of sound in the room; that is, the intensity level
would be reduced 10 db.
Thus it is possible to compute the noise level in the room if the intensity
of noises entering the room or generated in it are known.
It will be seen that the noise intensity reduction is dependent upon the
amount of sound absorption in the room, and that the first units of absorp-
tion are more effective than succeeding units. In general, the room noise
level will be from 10 to 20 db lower than the air inlet or outlet noise
intensity, the 10 db being in the case of bare rooms having large venti-
lating or air conditioning openings in relation to their size, and the 20 db
in the case of rooms having large amounts of absorptive material with
small openings. In some cases, the noise level reduction may run up to as
much as 30 db, but then the higher sound intensity adjacent to the
openings tends to nullify the effects of the extra reduction. Where these
openings are large, the local effect on the noise intensity extends some
distance from the opening; for instance, a four-square-feet opening might
have a local effect within ten feet, while a one-half-square-foot opening
would have a local effect within only five feet.
The coefficients of sound-absorption for a number of standard absorp-
tive materials used, or suitable for use, in equipment rooms are given in
Table 2. Coefficients are given for frequencies of 128, 512, and 2048
cycles. Where the frequency of the noise is not known, the values for
512 or 128 cycles are usually used.
INSULATION OF AIR-BORNE SOUND
The transmission of air-borne sounds through rigid partitions is accom-
plished primarily by the diaphragm-like vibrations of the partition. The
weight per square foot of the wall is the determining factor, and the
insulation value of a wall, in terms of the transmission loss in decibels,
is proportional to the logarithm of the weight per square foot. Other
factors, such as size, stiffness, composition, manner of mounting, and the
use of multiple structures separated by air spaces or flexible connectors,
contribute to the effective insulation. If the coefficients of sound trans-
mission of different types of structures and tjhe noise intensity in the space
adjoining a room are known, it is possible to calculate the noise intensity
in a room by the use of formula 1 and the following formula:
Jl = /»T (3)
304
CHAPTER 18 — SOUND CONTROL
TABLE 2. COEFFICIENTS OF SOUND ABSORPTION
MATERIAL
THICKNESS
COEFFICIENTS OP SOUND ABSOBPTION
UNCHES)
128
Cycles
512
Cycles
2048
Cycles
Acoustex 60, spray painted 1
0.16
0 51
0.72
Acousti-Celotex, Single B %
0.11
0.45
0.68
Acousti-Celotex, Triple B 1%
0.20
0 75
0.67
Acoustic Flexfelt—
0.27
0.56
0.68
Acoustone 1
0 66
0.69
^Vkoustolith plaster 3^
0.21
0 29
0 37
Akoustolith A, Tile 1
0.14
0.48
0.83
Brick wall, unpainted 18
0.024
0 031
0 049
Calicel 1
0.23
0.72
0.71
Corkoustic, Type C 1J^
0.08
0.61
0.64
Glass
0.035
0.027
0.020
Insulite Acoustile, Type 44 1^
0.26
0 50
0.61
Kalite, with three coats lacquer ... M
0.35
0.43
0.45
Macoustic Plaster, stippled to depth of % in 3^
Masonite ... Jfg
0.13
0.18
0.31
0.32
0.58
0.33
Plaster, gypsum on hollow tile. „
0.013
0.020
0.040
Plaster, gypsum, scratch and brown coats on
metal lath on wood studs
0.020
0.040
0.058
Plaster, lime, sand finish, on metal lath %
Poured concrete, unpainted
0.038
0.010
0.060
0.016
0.043
0.023
Rockoustile .... 1
0.18
0.57
0.72
Sabinite /^
0.34
0.49
Sanacoustic Tile 1J£
0.19
0.79
0.74
Stuccoustic Plaster, Type XB %
0.29
0.59
0.72
Transite Tile i 1
0.19
0.81
0.72
Trutone Tile 1%
0.31
0.57
0.64
Wood sheathing, pine . \ %
0.098
0.10
0.082
Wood, varnished . 1
i
0.05
0.03
0.03
^Architectural Acoustics, by V. O. Knudsen, pp. 219, 220, 240-251.
where
711 ~ noise intensity in space adjacent to room.
T — coefficient of sound transmission.
Coefficients of sound transmission for some common walls are shown
in Table 3.
Example 1. Suppose the brick wall between an equipment room and an adjacent
auditorium has an area of 200 sq ft and a coefficient of sound of 0.00001 (see Table 3) ;
that the auditorium contains 2000 sabines2 of absorption ; and that the noise level in
the equipment room is 70 db above zero level.
rii
70 - 0 = 10 logio -y- (from Formula 1)
Tfl
* = 1Q7
~ = 107 X 0.00001 = 100 (from Formula 3)
lo
100 X
= 10 (from Formula 2)
2 A sabine is 1 sq f t of totally absorptive surface.
305
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Room loudness = 10 logio 10 = 10 db
If the sound absorption in the auditorium had been as small as 200 sabines, the sound
intensity in the auditorium would have been 10 times as great and the noise level in the
auditorium would have been 20 db.
If the rest of the auditorium has an area of 20,000 sq ft with a surrounding noise
intensity of 50 db (/" = 105) the noise level due to all of the noise entering through the
wall would be found as follows:
-^- = 105 X 0.00001
10 (Through equipment wall) -j- 1 X
20,000
2000
= 20
Room loudness X 10 logio 20 = 13 db
Now suppose that there is also a duct having 20 sq ft outlet connecting the room with
apparatus having a noise level of 70 db (/" = IO7) and suppose that there is an assumed
ttenua tion in the duct equivalent to a transmission factor of 0.0002. Then,
IO7 X 0.0002 = 2 X IO3
-f- » 20 (from above) + 2 X IO3 X
20
2000
40
Room loudness = 10 logio 40 = 16 db
It may be seen how the energies of noises entering a room are added to obtain the
final room noise intensity.
The average coefficients of sound transmission (128 to 4096 cycles) for
a number of walls and of floor and ceiling partitions are listed in Table 3.
TABLE 3. AVERAGE COEFFICIENTS OF SOUND TRANSMISSION FOR BUILDING PARTITIONS*
DESCRIPTION OF PARTITION
AVERAGE
COKFFICIBNT
Brick panel, Mississippi, 8 in.; plastered both sides gypsum brown coat,
smooth white^finish; good workmanship
Brick wall, 2j^-in. plaster both sides
Brick wall, 2J^-in., 2-in. furring strips, J^-in. rigid insulation lath plastered
both sides „
Brick wall, 4 in., 2-in. furring strips and J4-in. rigid insulation lath, plaster,
on one side; other side plastered directly on brick. _
Concrete flat slab floor construction, reinforced; floating floor consisting
of nailing strips, rough and finish flooring; J^-in. rigid insulation furred
out and applied as ceiling.
Glass, plate ££-in.
Glass, plate M-in. double glazed, IJ^-in. separation
Metal lath, double, on IJ^-in. channels, M-in* gypsum plaster; without
cross bracing dips; 4 in., connected at edges only
Tile, hollow clay partition, three cells, 4 in. x 12 in. x 12 in., wood furring
strips, J^-in. rigid insulation, gypsum brown coat, smooth white finish
Wood joists, lower side plastered on wood lath; floating floor consisting of
nailing strips, rough and finish flooring.
Wood studs, four-paper plaster board, three-coat smooth finish gypsum
plaster „
Wood studs, two $4-in. sheets rigid insulation both sides, joints filled,
gypsum scratch and brown coats, smooth white finish
Wood studs, 2 in. x 4 in., staggered, metal lath, J^-in. gypsum plaster;
7 J£ in. ; connected at edges only
0.000010
0.000032
0.0000016
0.0000040
0.0000020
0.0010
0.0001
0.000016
0.0000050
0.0000050
0.000010
0.000013
0.000040
*Archiieciu al Acoustics, by V. O. Knudsen, pp. 308-322.
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CHAPTER 18 — SOUND CONTROL
LOCATION AND INSULATION OF EQUIPMENT ROOM
The equipment room, if possible, should be located at a considerable
distance from all rooms in which quiet is required. If this is not possible,
it is necessary to provide a high degree of insulation against the noise
which may be transmitted through the walls of the equipment room, and
also against the noise which almost certainly will be communicated
through the short ducts. (See discussion of Control of Noise Trans-
mission through Ducts, p. 311.) Three wall sections and two floor and
ceiling sections which are satisfactory for the wall insulation of the
equipment room are shown in Fig. 2. Other partitions, with their sound
insulating values, are listed in Table 3. The addition of absorptive
materials (such as are described in Table 2) to the inner walls and ceiling of
the equipment room will not only increase the insulation through the
walls, but will also reduce the intensity of the noise in the room. The
equipment room noise intensity may be figured in the same way as that of
the conditioned space, taking the equipment as the source of noise. In
case the equipment is subject to considerable vibration it is advisable to
provide a separate or floated floor.
- 4" Brick
Plaster
insulation Value =47 db.
- 4" Hollow Clay Tile
1"*
L"* 2" Furnng Strips
s Paper and Metal Lath
^Piaster
Insulation Value = 52 db.
-Absorptive Blanket
2 Fibre Board
S?" Plaster
\ 2
x Staggered Wood
Studs
Insulation Value
Greater than 50 db.
Finish Ftoonng
Absorptive Blanket
Plaster on Lath
Insulation Value = 50 db.
Flooring
Resilient Chairs
x Concrete Slab
Resilient Hangers
'Plaster on Lath
Insulation Value - 60 db., or more
FIG. 2. THREE WALL SECTIONS AND Two FLOOR AND CEILING SECTIONS WHICH ARE
SUITABLE FOR THE INSULATION OF EQUIPMENT ROOMS*
aAcoustical Problems in the Heating and Ventilating of Buildings, by V. O. Knudsen (A.S.H.V.E.
TRANSACTIONS, Vol. 37, 1931).
INSULATION OF MACHINERY AND SOLID-BORNE VIBRATION
Since mechanical vibrations are readily transmitted through the solid
structure of a building, it is extremely important in air conditioning that
all mechanical equipment in which vibrations are generated be thoroughly
insulated from the solid structure of the building. An almost universal
notion prevails that the vibrations generated by machinery can be in-
sulated from a building simply by placing a slab of cork or a layer of
hair felt between the machinery and the floor of the room. If the machinery
is sufficiently heavy, and the cork or felt sufficiently resilient, this ex-
pedient may suffice. On the other hand, if the machinery is not suf-
307
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
ficiently heavy to load the cork or felt support to the extent that the
natural frequency of the machinery on the cork or felt is low in com-
parison with the frequency generated by the equipment, the cork or felt
may be of little avail. The insulation of vibration can be accomplished
by means of suitable elastic supports or suspensions, but the design of
these elastic supports should be based upon calculation rather than
guess-work.
The theory of the insulation of vibration was first worked out by
Soderberg3. If a machine of mass m be supported by an elastic pad the
amount of vibratory force communicated by the machine to the floor or
foundation upon which it rests will be determined by the elastic and viscous
properties of the pad. The ratio of the vibratory force communicated to
the floor or foundation with the machine resting upon the pad, and with
the machine resting directly upon the floor, is given by the following
equation :
/ r. | j 1^
f4)
where
•tr = the so-called transmissibiltty of the support.
c = the compliance (that is, the reciprocal of^the force constant).
r — the mechanical resistance owing to the viscous forces within the support.
n — the frequency of vibration generated by the machine which is to be insulated,
such as the commutation frequency of a motor or the blade frequency of a fan.
m — the mass of the machine to be insulated.
It should be noted that not only must vibrations within the audible range of fre-
quencies be considered, but those in the sub-audible range as well, since these may cause
objectionable vibrations. All the possible frequencies should be considered in the calcu-
lation. Sometimes beat effects are introduced by slight irregularities of belts or pulleys
that have much lower frequencies than those of the rotating elements.
If the pad is to be of any value in the prevention of solid-borne vibra-
tions, the value of T! must be considerably smaller than unity. If the
fundamental frequency of vibration generated by the machine happens to
coincide with the natural frequency of the mass of the machine resting on
the elastic pad, a condition of resonance will be established, and the
machine will exert a greater force upon the foundation than it would if
the pad were completely removed. It is necessary, therefore, that the
elastic support be sufficiently compliant, and the mass of the machine
sufficiently heavy, that the natural frequency of the mass m upon its
elastic support will be low in comparison with the frequencies which are
generated by the machine. Thus, if the principal vibrations in the
machine be of the order of 100 vibrations per second, the natural frequency
of the machine mounted on its elastic support should not exceed about
20 vibrations per second.
If a slab of insulating material be placed under the entire foundation of
a machine, as is often done in practice, it may happen that the natural
frequency of the machine on its elastic support will be nearly the same as
the frequencies which are to be insulated, in which case the elastic support
»C. R. Soderberg, The Electric Journal (January, 1924), and succeeding articles. See also V. O. Knudsen,
Physical Review, Vol. 32, 1928, p. 324, and A. L. Kimball, Journal Acoustical Society of America, Vol 2,
1930. p. 297.
308
CHAPTER 18 — SOUND CONTROL
will be worse than nothing. In general, as Equation 4 shows, both m and
c should be as large as possible if the vibrations of the machine are to be
effectively insulated from the solid structure of the building. Further-
more, the machine should rest upon a rigid floor so that the elastic
yielding of the floor is prevented from communicating the machinery
vibrations to the solid structure of the building.
The elastic support under the machine acts as a low-pass filter which
passes all frequencies below about two times the natural frequency of the
machine mounted on its elastic support, but prevents all frequencies
above about V .??? from reaching the solid structure of the building. The
principal influence of the internal mechanical resistance r is to limit the
vibration at the resonant frequency. It is generally advisable, therefore,
to use materials which have an appreciable internal resistance.
The values of c and r can be determined for any specimen of flexible
material and, when known, can be used to determine the insulation value
of any particular set-up. The value of c can be obtained by making static
measurements of the amount of displacement of the compressed support
for each additional unit of the compressing force. If this be done for a
specimen of the flexible "material of a certain thickness and area of cross
section, the compliance can be determined for any other thickness or area
from the relation that c will be directly proportional to the thickness and
inversely proportional to the area of the flexible support. When the
internal resistance r is not too large, it can be determined by observing the
successive amplitudes of the free vibrations of a mass m which rests upon
a specimen of the flexible material, and solving for r by the usual log-
decrement method. Or, if the damping be so great that the free motion of
m is non-oscillatory, r can be obtained from measurements on the experi-
mentally-determined resonance curve of the forced vibrations of m, or
from measurements of the rate of return of m when it is given an initial
displacement.
If the resistance of a certain specimen of material, as cork, felt, or
rubber, has been determined by any of these methods, the resistance for
any other thickness or area of the material can be determined approxi-
mately because the resistance will be inversely proportional to the
thickness and directly proportional to the area of cross-section of the
flexible support. Thus, if the values of c and r for a flexible material
be known, it is possible to calculate, by means of Equation 4, the amount
of insulation that will be obtained from the use of this material as a
flexible support for a piece of equipment having a mass m. For the
routine calculations in practice, r may be neglected with only a slight
sacrifice of accuracy. Table 4 gives the values of c and r for a number of
commonly used flexible materials.
In general, there are two principal points to observe in the design of a
flexible support for any piece of equipment, namely, the material should
have a relatively large compliance and it should be loaded to nearly the
upper safe limit of loading. Several flexible metallic supports have recently
been developed.
Example 2. A machine weighing 1000 Ib has a base area of 20 sq ft. Assume that the
principal vibration of the machine has a frequency of 100 cycles per second (most
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 4. COMPLIANCE AND RESISTANCE DATA FOR TYPICAL SPECIMENS OF
FLEXIBLE MATERiALSa
The compliances and resistances given in the table are for specimens 1 in. thick
and 1 sq cm in cross-section
MATERIAL
DESCRIPTION
OF MATERIAL
APPROXIMATE UPPEB
SAFE LOADING IN
POUNDS PER SQUARE
INCH
COMPLIANCE c IN
CENTIMETERS PER
DYNE
RESISTANCE r IN
ABSOLUTE UNITS
Corkboard
Corkboard
Flax-li-num
Celotex
l.lOlbper
board foot
O.TOlbper
board foot
1.351bper
board foot
Carpet lining
12
8
4 to 6
10
0.25x 10~6
0.50x 10~6
0.60x10-'
0.40 x 10~6
O.lox 105
0.25x 105
O.oOx 10*
Celotex
Insulating
12
0.18 x 10~6
Insulite
board
Insulating
15
0.16x 10-*
Mason it e
board
Insulating
15
0.12x 10-«
Anti-Vibro-Block
Sponge Rubber
board
"25~l"b"per"
5
1 to 3
0.60x 10~6
3.6 x 10~6
1.5 x 105
Soft India Rubber
cubic foot
55 Ib per
3 to 6
1.2 x 10~6
Hairfelt
cubic foot
10 Ib per
1 to 2
1.5 x 10~6
cubic foot
^Architectural Acoustics, by V. O. Knudsen, p. 278.
machinery vibrations are less than 150 vibrations per second, and the assumed frequency
of 100 is quite representative of typical machines). Suppose that a 1-in. slab of cork-
board weighing 1.10 Ib per board foot be placed between the machine and the floor.
The loading on the cork will then be only 50 Ib per square foot, or slightly more than
% Ib per square inch. (It is assumed that the compliance c in centimeters per dyne for a
specimen 1 in. thick and 1 sq cm in cross-section is 0.25 X 10~6 and the resistance r in
mechanical ohms is 0.15 X 10s.)
The transmissibility is calculated in the following manner:
Mass of machine in grams = 1000 X 454 = 4.54 X 10&.
Area of base in square centimeters = 20 X 144 X
2.54 X 2.54 = 1.86 X 104.
Therefore, the compliance of the entire support, 1 in. thick and 20 sq ft in cross
section, is 0.25 X lO"6 X -T-^-TT-T^T = 0-134 X lO"10 cm per dyne, and the resistance of
l.&o X lu*
the entire support is 0.15 X 10fi X 1.86 X 104 = 0.28 X 109 mechanical ohms (or absolute
units). Therefore,
V
<°-28 X
+
X 100 X 0.134
(0.28 + 109)2 4- (2x X 100 X 4.54 X 106 -
= 0.93
2-rc X 100 X 0.134
Consequently, it is seen that the transmissibility is nearly equal to unity, and that the
support therefore is not satisfactory for insulating 100 or fewer vibrations per second.
If the amount of cork be reduced so that it is loaded to 10 Ib per square inch, the total
area of the supporting cork will be only 100 sq in. or 645 sq cm. The compliance of the
310
CHAPTER 18— SOUND CONTROL
entire support will now be 0.25 X lO"6 X ^ » 0.39 X 10~fl cm per dyne, and the
resistance will be 0.15 X 105 X 645 - 0.97 X 107 mechanical ohms (or absolute units).
Therefore
-v
(0.97 X 107)2 -f 10
X 100 X 0.39
(0.97 X 107)* + ( 2x X 100 X 4.54 X 10s - 10*
X 100 X 0.39 /
It is seen, therefore, that with the bearing surface on the cork reduced
to 100 sq in. (that is, with the cork loaded to 10 Ib per square inch), the
transmissibility is reduced to 0.037, or the amplitude of vibration trans-
mitted to the floor will be only about 1/27 of what it would be if the
machine were mounted directly upon the floor. These two numerical
examples will serve to show not only the manner of making the calcu-
lations, but also the importance of selecting the proper type and design of
flexible supports for insulating the vibrations of a machine from the
rigid structure of a building.
CONTROL OF NOISE TRANSMISSION THROUGH DUCTS
The most troublesome sources of noise from ventilating and air con-
ditioning equipment are fan and motor noises which are transmitted
through the ducts. The reduction, in decibels, of noise transmitted
through a duct, neglecting reflection from ends and bends, is proportional
(1) directly to the length of the duct, (2) directly to the perimeter of the
duct, (3) inversely to the area of cross-section of the duct, and (4) directly
(or at least approximately so) to the coefficient of sound absorption of the
material which comprises the interior surface of the duct. It is apparent
therefore that long narrow ducts, lined with highly absorptive material,
will provide a high degree of insulation against the transmission of noise
through ducts. In fact, small ducts (4 in. x 6 in.), made of material
having a coefficient of sound-absorption of 0.50, will provide a noise
reduction of slightly more than 1 db per linear foot.
As can be seen from an inspection of Table 2, noises of low frequency
are difficult to absorb; on the other hand, these frequencies are easily
reflected by elbows, branches, and duct ends whereas higher frequencies
are little affected. Furthermore, the reflection effects are more pro-
nounced in small ducts than in large ducts. Hence, by introducing into
a duct a sufficient length of small, absorptive channels together with a
number of elbows or other reflecting elements it is possible to reduce the
transmitted noise to any required degree. This applies not only to ducts
between the equipment room and other rooms in a building, but also to
ducts connecting adjacent or nearly adjacent rooms. By the proper use
of such filters it is possible to eliminate all of the difficulties which arise in
connection with the transmission of sound through ventilating ducts. The
problem is an engineering one which can be worked out prior to the in-
stalling of the equipment, and it can be calculated in such a way as to
meet the most rigorous demands for silent operation. There is a need for
quantitative data regarding the attenuation or noise-reduction provided
by different types of ducts, but even with the meager data available it is
311
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
possible to design filters which will suppress the ordinary noises incident
to the ventilating or air conditioning of buildings4.
In general, the motion of air resulting from the ventilating of rooms is
not sufficient to introduce any appreciable difficulty in auditoriums, except
where noise may originate from the issuing of high-speed air from nozzles.
However, by proper stream-lining of the nozzles, it is possible to work
with speeds which are adequate for all practical purposes without pro-
ducing any disturbing noises. Since sound is propagated with a velocity
of more than 1100 fps, the velocity of the air would have to attain speeds
of at least 20 to 30 fps before these wind velocities would have any
appreciable influence upon the propagation of sound.
If there is to be any appreciable motion of air in an auditorium, it is
advantageous to have the upper layers of air moving in a direction from
the stage toward the audience, as this will tend to refract the sound waves
down toward the audience. However, unless the speed of the air is as
great as 20 or 30 fps, the amount of refraction will not be noticeable.
Therefore, as a rule the motion of air in an auditorium does not have an
appreciable effect upon the acoustical properties of the room.
EFFECT OF HUMIDITY UPON ACOUSTICS
Recent experiments5 have shown that both the humidity and the tem-
perature of air have a marked influence upon the rate of absorption of
high-pitched sounds. Perfectly dry air is less absorptive than air con-
taining any amount of water vapor. At relative humidities of 5 to 25 per
cent, the air is highly absorptive but becomes less and less absorptive as
the humidity is increased. High-frequency sounds are propagated
better in cold humid air than in hot dry air, and since high-frequency
sounds are particularly important for the preservation of good quality
in speech and music it is advantageous to maintain the air in a room at a
relatively high humidity, not less than about 55 to 60 per cent. On the
other hand, where it is desirable to absorb all frequency components of
sound, as for the reduction of noise in offices, it is advantageous to main-
tain relatively dry air.
The time of reverberation in a room is given by the following equation :
. = 0.0497 ,
Sloged - a)
where
V = volume of room in cubic feet.
S — interior surface of room.
a = average coefficient of sound-absorption of the interior surface of the room.
m — the absorption coefficient of the air in the room.
The coefficient m depends upon the frequency of the sound and the
humidity (and probably the temperature) of the air. At a temperature of
70 F, and for sound waves having a frequency of 4096 vibrations per
second, m = 0.0027 at 25 per cent relative humidity, 0.0018 at 54 per
*How Sound is Controlled, by V. O. Knudsen (A.S.H.V.E. TRANSACTIONS, Vol. 37, 1931).
^Effect of Humidity upon the Absorption of Sound in a Room, by V. O. Knudsen (Journal Acoustical
Society of America, July, 1931). Also see report presented at the May, 1933, meeting of A. S. of A.
312
CHAPTER 18 — SOUND CONTROL
cent, and 0.0013 at 82 per cent. It will be seen, therefore, that the absorp-
tion of sound in the air is twice as great at a relative humidity of 25 per
cent as it is at a relative humidity of 82 per cent. This explains why
sounds in the open travel so much better on humid days than they do on
dry days. Although this dependence of absorption upon humidity is
characteristic of low-frequency as well as high-frequency sound, the actual
amount of absorption in the air is negligible for frequencies below about
1024 vibrations per second. However, the absorption of the higher
frequencies in the air is a significant factor, and its dependence upon
humidity calls for careful consideration in planning the air-conditioning
equipment for buildings.
PROBLEMS IN PRACTICE
1 • What are the requirements for good hearing in a room?
Freedom from noise, adequate loudness of speech or music, uniform distribution of
sound throughout the room, freedom from echoes and sound foci, no pronounced reso-
nance, and proper reduction of reverberation.
2 • Why do modern improvements in the acoustics and air conditioning of
buildings present new acoustical problems to the heating and ventilating
engineer?
In acoustically treated rooms, both outside and inside noise are reduced, and conse-
quently the noise of ventilating equipment becomes more noticeable. The closed
windows in air conditioned buildings exclude outside noise, which makes all inside noise
from mechanical equipment seem louder.
3 • Name the acoustical problems which should be solved in connection with
the installation of heating or air conditioning equipment.
Selection of quietly operating equipment; adequate insulation of walls surrounding the
equipment room; mounting of all vibrating equipment on flexible supports which will
eliminate solid-borne vibrations; design of suitable sound filters to reduce the trans-
mission of noise through ventilating ducts; the use of suitably low air speeds and stream-
lining, where necessary, to prevent eddy noises.
4 • Are good heat insulators also good sound insulators?
As a rule, no. Blankets and felted materials offer considerable insulation for sounds of
high frequency, but very little for sounds of low frequency.
5 • What is the principal consideration in the selection of elastic supports for
the insulation of machinery vibration?
The support should be so compliant that the natural frequency of the mass of the machinery
on its elastic support will be low in comparison with the vibrational frequencies which are
to be insulated.
6 • What means should he utilized for preventing air-borne noise from the
ventilating equipment from being transmitted through the walls, ceiling, or
floor of the equipment room?
Treat the interior walls and ceiling of the equipment room with absorptive material ; see
that all doors and windows to the equipment room fit tightly in their frames; and use
wallr and floor and ceiling partitions which have an insulation value of not less than 50 db.
313
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
7 • Name effective methods for reducing the transmission of sound through
ventilating ducts.
Line the ducts with sound absorptive material, or use suitable sound filters made up of
long channels of small cross-sectional area, lined with sound absorptive material.
8 • What are the effects of humidity and temperature on the absorption of
sound in air?
The absorption increases with a rise in temperature, and decreases for relative humidities
above about 20 per cent. A relative humidity of 55 to 60 per cent is advantageous
acoustically in large auditoriums.
9 • How may sound be measured and what are the advantages of the methods
available?
Three practical methods are now available to the heating and ventilating engineer,
namely:
a. The noise meter method.
b. The audiometer and ear method.
c. The tuning fork and ear method.
Except for instrument adjustments and the use of the eye in reading a meter, the human
element does not enter into measurements made with the noise meter, so it is to be pre-
ferred, if available. The tuning fork method is relatively cheap and simple and suf-
ficiently accurate for most field work. The audiometer and ear method ranks between
these two in preference.
10 • What are some of the more important sources of noise in buildings, for
which the heating and ventilating engineer may be held responsible?
a. Furnace room equipment.
b. Radiators and piping.
c . Uncalked openings in walls around pipes and ducts,
d. Ventilating fans, if noisy in operation and not isolated from the building structure by
properly designed vibration damping foundations.
e. High air velocity in ducts.
/. Ventilation fan rooms not insulated acoustically from parts of the building where
noise would be objectionable,
g. Ventilating ducts without flexible non-metallic sleeves in them to break metallic
sound conducting paths.
h. Cross connection of rooms acoustically through ducts.
i. Ventilating ducts without sound absorbing lining, if required.
j. Unit heaters and ventilators.
k. Unit air conditioners.
11 • The noise level in the fan room, directly under the main floor of a theater
is 70 db. The floor is constructed as described in Item 5, Table 3. What is the
fan noise level in the theater?
According to Table 3, the average coefficient of sound transmission, t, of such a floor
construction is 0.0000020. The transmission loss through the floor, expressed in db, is:
TL
= 10 logic
gl° 0.0000020
57
The fan noise level in the theater would, therefore, be 70 db less 57 db, or 13 db, which,
according to Table 1, is an acceptable level.
Another way of arriving at the same result is by use of Formula 3r in which V is the in-
314
CHAPTER 18 — SOUND CONTROL
tensity of fan noise as measured in the theater, and /" its intensity as measured in the
fan room, I0 being the reference intensity in both cases, while -r is 0.000002 or 2 X 10-6.
j- = 10'
P
Noise level = 10 logio 20 - 13 db.
107 X 2 X 10-6 = 20
•to
12 • Measurements made separately of the noises from different sources pre-
vailing in a large, noisy banking room revealed the following average noise
levels:
a. From the street through windows, doors, and walls, 40 db.
b. From adding machines, typewriters, human movements and conver-
sation, 60 db.
c. From the ventilating system, 50 db.
What was the total noise level of the room?
Calling Js, /b, and /v the intensities of the street, banking room, and ventilation noises,
respectively, and J0 the reference level, we have:
/o ~7o~ !o
The total intensity, I, will be 7S -}- Ib -f 7V
The intensity level is 10 logio -j-
° =101og10^dl^±_/v)
= 10 Iog10 (104 + 106 -f- 105)
- 60.4 db
Note that the total loudness level is not much above the level of the loudest noise. While
noise intensities may be added arithmetically, noise levels expressed in decibels cannot
be so added.
13 • A ventilating fan room 30 ft by 30 ft by 12 ft has brick walls, a concrete
floor, and a concrete ceiling. How much will the noise level of this room,
expressed in decibels, be reduced by applying sound insulating material (co-
efficient of absorption 0.6 at 512 cycles) to two walls and the ceiling?
Use Formula 2:
PS1
I = before applying material
PS1
/i — — f- after applying material
PS1
JL = a = J*!_
It PS1 a
a'
Referring to Table 2:
a = (4 X 12 X 30 X .031) + (2 X 30 X 30 X .016) = 73.4
a' = (2 X 12 X 30 X .031) + (30 X 30 X .016) -f (2 X 12 X 30 X 0.6) +
(30 X 30 X 0.6) = 1008.7
/ a1 1008.7
Ji a 73.4
13.7
Noise level reduction = 101og1P-=- = 10 log™ 13.7 = 11.4 db.
315
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
14 • What relation does the movement for the suppression of noise bear to the
trend toward air conditioning of offices and other places in cities where people
work or congregate?
Very important sources of disturbing sounds are the various street noises that gain
entrance, not only through open windows but to a certain extent even through closed
windows. If windows are to be kept closed to exclude noise, air conditioning is a practical
necessity, especially in summertime. Summertime air conditioning makes use of
awnings, 'which are not only desirable but economical in that they keep down cooling
loads. To obviate condensation and frost on windows, wintertime ^air conditioning calls
for storm sash or double glazing which in turn reduces the transmission of street noises
316
Chapter 19
AIR DISTRIBUTION
Warm Air Systems, Combined Systems, Split Systems, School
Buildings, Theaters, Upward System, Dowmoard System, Vanes
-HTX) produce proper air distribution in a room to be ventilated, heated,
JL or cooled by air, the design and location of the air supply inlets and
exhaust outlets must be carefully considered. A system may fail though
it handles the proper amount of air if such important design principles
are ignored.
WARM AIR SYSTEMS
With gravity warm air systems, it has been the practice to place the
supply registers in or near the floor of each room and to place the return
grille in the floor of the first story. When there is mechanical air circu-
lation, the supply ducts may be extended to the outside walls and the air
discharged into the rooms near their cold exposures; on the return side a
grille is placed in or near the floor at a central location, or individual
return grilles are provided, usually at the corner of the room opposite the
supply register.
These arrangements are usually satisfactory for heating (Fig. 1) but not
for cooling (Fig. 2). If cool air is introduced at one side of the room at the
floor, and if the escape opening for the heated air to be displaced by the
cool air is at the floor at the other side, the cool air will travel across the
floor and escape through the vent or return air opening, and thus not
appreciably affect the warmer air in the upper part of the room.
The air supply opening will serve satisfactorily if located high on an
interior wall opposite the exposed wall, and this location answers well also
for gravity indirect heating. The corresponding return air arrangements,
however, apparently are not subject to exact rules, but must be adapted
to circumstances. For example, where the building is compact, with a
first story having rooms open to each other, a single, centrally-located
return at the floor functions satisfactorily for heating, and if the second
story bedrooms are also compactly arranged no individual return from
each will be necessary. On the other hand, any room which is unusually
exposed, which is especially remote with reference to the other rooms, or
which is apt to be tightly closed most of the time, should have a controlled
return grille and duct. With a mechanical warm air system, this return
may be close to the floor, either below the supply grille or under windows
or other cold exposures, and with a gravity system it may be close to the
floor at the opposite side of the room from the supply grille.
There is always an advantage in keeping the warm air ducts concen-
317
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
trated nearer the furnace and not exposing them to the influence of back
drafts of cold air by locating them in outside walls.
COMBINED SYSTEMS
For a combined mechanical heating and cooling system using refrigera-
tion for cooling, no particular change in the ducts usually is necessary. It
is desirable from an economic standpoint to take advantage of the natural
tendency of the cooler air to remain below the warmer air overhead, and
anything which will bring about such stratification will effect an economy
in refrigeration.
FIG. 1. AIR CIRCULATION WHEN HEATING
WITH Low SUPPLY AND RETURN OPENINGS
FIG. 2. AIR CIRCULATION WHEN COOLING
WITH Low SUPPLY AND RETURN OPENINGS
FIG. 3. AIR CIRCULATION WHEN COOLING
WITH HIGH SUPPLY OPENING AND
Low RETURN OPENINGS
FIG. 4. SECTION THROUGH AW ELEMENTAL
MECHANICAL WARM AIR HEATING-
COOLING SYSTEM. THE ATTIC
FAN is ALTERNATIVE
If the return ducts of a mechanically operated warm air system are
adequate, appreciable cooling may be accomplished as follows: The fan
outlet must have a by-pass leading to a basement window or to a chimney
provided for the purpose and the return duct must have an alternative
shaft opening into the highest part of the house. At night, in summer, the
fan may be operated to exhaust the hot air from the top of the house by
the return air duct just described and the fan will blow this heated air out
of doors through the window, or preferably, of course, through the
chimney. The cooler night air must then enter the house through the
318
CHAPTER 19 — AIR DISTRIBUTION
windows, and by its motion and temperature will extract the heat from
the walls and furniture. The cost of power for such cooling should be
carefully checked against operating with a much smaller volume of air
mechanically cooled.
Fig. 3 shows the air circulation when cooling with a high supply opening
and a low return opening. The air circulation, when heating, will be
substantially the same as when cooling. Fig. 4 shows a section through
an elemental mechanical warm air heating-cooling system. The attic plan
is alternative. Summer night cooling may, of course, be accomplished
by placing an exhaust fan in the attic.
SPLIT SYSTEMS
Many buildings which are heated by radiators or convectors and which
have rooms requiring ventilation or cooling have air supply and exhaust
systems independent of the radiators or convectors. Such installations
are termed split systems. When the air enters a room through conventional
side wall inlets an occupant may feel comfortable if the air is about the
temperature of the room, but the introduction of too cool air may cause a
feeling of draft. To correct this draft condition, glass chutes and elabor-
ate diff users are sometimes provided. The arrangement shown in Fig. 5
for supplying cool air to a room provides satisfactory air circulation in
spaces up to 400 sq ft in area with ceilings as low as 8 ft. There is no
maximum ceiling limitation as to height.
When the room in question is provided with a unit ventilator which
obtains its air supply directly through the wall from out of doors, the
distribution with a high velocity air jet passing in an upward direction
is quite satisfactory.
The use of unit air conditioners for summer cooling introduces no new
features or difficulties which have not already been encountered in winter
heating. Conditioners must be provided with positive control by means of
valves or dampers, or both, which will prohibit any sudden and wide tem-
perature variation, and keep the entering air not more than approxi-
mately 7 deg cooler than the air already in the space. This temperature
margin is dependent on various factors including the ceiling height of the
room and the velocity of the air at the discharge grille.
SCHOOL BUILDINGS
The air distribution conditions in school building classrooms are not
unlike those illustrated in Fig. 1 for mechanical warm air systems and
those in Fig. 6 for unit ventilator equipped plants. School rooms which
have center-ceiling inlets along the lines of Fig. 5 have given excellent
results. It is important that the temperature of the entering air, whether
this air be supplied by a local unit ventilator or by a distant central fan,
be controlled so that the air cannot enter the room from a side-wall inlet
or from a unit ventilator at a temperature more than a very few degrees
cooler than that of the air already near the ceiling of the room.
Fig. 7 shows a section through a room equipped with a unit air con-
ditioner or unit cooler. This is typical of the condition in effect when any
recirculating room-cooling unit is installed.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Most unit ventilators employ a unique method of air distribution. Its
principal feature is that the air is discharged at a high velocity toward the
ceiling, with the jet inclined slightly toward the room in order to dis-
tribute the air over the ceiling. In designing a unit ventilator installation
great pains should be taken that nothing will interfere with the operation
of this jet. For this reason unit ventilators should never be installed
where there is a beam on the ceiling running at right angles to the direction
of the air jet. If ceiling beams cannot be avoided, the unit ventilator
should be placed to discharge parallel to the beams.
wi
A
? Burred Ceding
T
FIG. 5. SECTION THROUGH A
RADIATOR-HEATED ROOM
FIG. 6. SECTION THROUGH A UNIT VENTI-
LATOR-EQUIPPED ROOM WHEN HEATING
FIG. 7. SECTION THROUGH A UNIT CON-
DITIONER EQUIPPED ROOM WHEN COOLING
FIG. 8. PLAN OF A CLASSROOM IN A
SCHOOL VENTILATED BY A CENTRAL FAN
In Fig. 8 the cloakroom ceiling is furred down so as to conceal the metal
air supply duct, which is close to the ceiling. The air for ventilation
usually is controlled by a duct thermostat near the fan, at a temperature
slightly higher than the temperature required in the room, to allow for
heat losses in the duct system.
THEATERS
Theaters are usually ventilated or cooled by introducing precon-
ditioned air. No ventilating system for a theater should be given con-
sideration without definite provision for cooling. Theater cooling
generally is far more important than theater heating. There are two
widely different methods of theater air distribution, the downward and the
upward.
320
CHAPTER 19 — AIR DISTRIBUTION
Downward System
Theaters usually are equipped with downward air distribution with
horizontal diffusion of the entering cool air so as to combine it, both as to
temperature and dilution, with the heated air which inevitably must rise
from the bodies of the patrons. The waste or the recirculated air is with-
drawn from the room at the floor. If the theater is large, and if the
exhaust openings are placed in the side walls at the floor, drafts may be
felt by the people who sit near the openings. There is no objection, how-
ever, except that of cost, to the use of small exhaust openings under each
seat. These may be cleanable floor grilles or may have mushroom covers.
In a downward system, if the entering cool air is not deflected hori-
zontally, it will fall through the surrounding much hotter air, and will
Supply Ducts
— '
Stage
FIG. 9. SECTION THROUGH A THEATER FIG. 10. THEATER WITH UPWARD SYSTEM
WITH DOWNWARD VENTILATION OF VENTILATION
reach high velocities by the time it strikes the heads of the occupants.
Air at a temperature 10 deg below that of the surrounding air is decidedly
objectionable when forced over one's head at a velocity of nearly 400 fpm.
Fig. 9 shows a section through a theater with downward ventilation.
The deflectors cause the entering cool air to be spread horizontally so that
it will mix with the hotter air. The final escape is through well-distributed
openings in the floor. There have been cases in which the downward
system of air distribution such as that illustrated in Fig. 9 gave trouble
due to overheating at the rear, both above and below the balcony,
especially when not provided with refrigeration for cooling, and when not
adequately controlled. It is especially necessary that adequate removal
of the heated air be provided at these low-ceiling points and it is probable
that auxiliary exhaust at or through the ceiling after the manner of the
arrangements shown in Fig. 5 would be helpful.
Upward System
If no inlet openings are possible in the ceiling, the upward system may
be the less objectionable alternative. Fig. 10 shows a section through a
theater with the upward system of air distribution. The occupants often
suffer from drafts due to the cool air which comes from the unoccupied
zones.
When the entire seating area is occupied, the upward system gives
little trouble when cooling, and since very little heating is required under
such conditions, practically no difficulty is encountered. The maximum
321
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
volume of air to be introduced with the upward system is about 25 cfm
of air per person at a low velocity, say at 150 fpm (linear), and at a tem-
perature not more than 6 deg below the room temperature. For partial
occupancy, higher entering air temperatures can be used with corre-
spondingly less danger from drafts.
VANES
In order to cause the supply air to a room to take a fixed or desired
direction when leaving the inlet opening of a flue, stationary vanes may
be provided at both the back of the grille and at the grille to direct the air
flow. Fig. 11 shows a section through a room inlet opening at the top of a
rising flue and indicates the air conditions when no vanes are used.
Fig. 12 shows a section through the same room inlet opening when vanes
are advantageously placed to direct the flow of air.
FIG. 11. Am CONDITIONS AT INLET
OPENING AT THE TOP OF A RISING FLUE
WHEN NO VANES ARE USED
FIG. 12. AIR CONDITIONS AT INLET
OPENING AT THE TOP OF A RISING FLUE
WHEN DIRECTIONAL VANES ARE USED
In many theater and commercial installations the ejector-like action
of high-velocity air emerging from a duct is taken advantage of, and
scientifically proportioned nozzles are installed to cause definite recircu-
lation of the room air.
PROBLEMS IX PRACTICE
1 • Is the conventional warm air system, employing floor or baseboard supply
registers, suitable for heating and cooling?
Floor or baseboard supply registers are suitable for heating service because the natural
tendency of warm air is to rise. They are not suitable for cooling because the natural
tendency of cool air is to stay near the floor and gradually work its way to the return
registers, thus not cooling the air in the upper part of the room. See Figs. 1 and 2.
2 • What type of air distribution system is suitable for heating and cooling a
home?
In order to provide satisfactory cooling without drafts it is necessary to discharge the
air at relatively high velocity toward' the ceiling from a high point, as shown in Fig. 3.
If the register is properly designed and the air capacity is limited to approximately
400 cfm, the cool air will mix with the air in the room before it drops to the occupied zone.
However, care must be taken that discharged air does not impinge on beams which would
cause the cool air to be deflected downward. This arrangenient is also satisfactory for
heating.
322
CHAPTER 19 — AIR DISTRIBUTION
3 • Why is the conventional low velocity side wall inlet unsatisfactory for
cooling purposes?
With the conventional side wall inlet using velocities of 300 to 400 fpm the discharged
air quickly loses its velocity and drops, causing drafts in the occupied zone.
4 • \£ hat method of side wall introduction is satisfactory for cooling purposes
with a 12-ft ceiling height?
The method shown in Fig. 3 can satisfactorily circulate air as much as 10 to 15 F below
room temperature, provided (1} each jet is limited to 400 cfm, <2) the outlet velocity is
high, (3) the air is directed toward the ceiling, and (4) there are no beams on the ceiling.
In order to employ this method in a classroom it is usually necessary to have at least
three inlets, but even with three inlets the cooling capacity is limited to that obtained
by circulating air at 10 to 15 F below room temperature.
5 • Should unit ventilators he considered as heating units or as cooling units?
Experience has shown that approximately 75 per cent of the time a classroom is occupied
the problem is one of cooling rather than one of heating. For this reason unit ventilators
should be considered as cooling units.
6 • What method of air distribution is usually employed with unit ventilators?
Most unit ventilators employ a unique method of air distribution in which the air is
discharged at a high velocity toward the ceiling. The air stream is usually inclined
toward the room.
7 • How should a unit ventilator he located in a. room that has ceiling beams?
When there are ceiling beams the unit ventilator should be so located that the beams will
be parallel with the direction of the air discharge in order that the beams will not deflect
the air downward.
8 • Wliat is the minimum temperature at which unit ventilators can distribute
air in a classroom without causing drafts?
Generally speaking, the lowest minimum discharge temperature at which objectionable
drafts will not be created is 60 F. Some designers suggest that the discharge temperature
can drop as low as 35 F below the room temperature without causing drafts when
units are properly installed.
9 • What is the usual method of ventilating school auditoriums and gym-
nasiums when unit ventilators are used in the classrooms?
If unit ventilators are used in classrooms the usual method of ventilating the auditorium
or gymnasium is to use one or more large units located above and on either side of the
stage.
10 • What is the maximum amount of air which should he discharged, from one
point in a school auditorium or gymnasium?
The maximum amount of air which should be discharged from one point is 5000 cfm.
This limitation applies whether the air is supplied by units or by a central fan from a
distant point.
11 • Are vents required in school classrooms, auditoriums, and gymnasiums?
With both the unit and the central fan systems, vents are usually installed as a certain
and positive means of disposing of the vitiated and odoriferous air and also, with the
central fan system, for the further purpose of effecting a means of partial recirculation.
Natural outward air leakage may take the place of vents, if and when it proves sufficient,
but it is usually uncertain, insufficient, and uneconomical. Vents are required by law
in some communities. If they are installed, they should be provided with dampers in
order that they may be throttled when required and closed at night and during holidays.
12 • What type of system is generally used in large continuously operated,
theaters?
323
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Most large continuously operated theaters are provided with complete downward
systems of air distribution similar to the one shown in Fig. 9. With this system a large
number of inlet openings is provided, each of which discharges air in a thin horizontal
stream at high velocity in order that the cool air will be mixed with the air in the theater
before it reaches the patrons.
13 • What system of air distribution is frequently used in smaller theaters?
The system used, particularly where artificial cooling is had, brings air in at high velocity
through a large number of small horizontal nozzles located in the rear of the auditorium
near the ceiling. This high velocity air mixes with a much larger quantity of air and
causes circulation within the theater before it comes into contact with the occupants.
With this method care must be exercised not to discharge the air against ceiling beams or
projections which may give a downward direction to the cool air before it is thoroughly
diluted.
324
Chapter 20
, AIR DUCT DESIGN
Pressure Losses., Friction Losses, Friction Loss Chart, Proportioning
the Losses, Sizes of Ducts, General Rules, Procedure for Duct
Design, Air Velocities, Proportioning the Size for Friction, Main
Trunk Ducts with Branches for Public Buildings, Equal Friction
Method, Details of Duct Construction
THE flow of air due to large pressure differences is most accurately
stated by thermodynamic formulae for air discharge under condi-
tions of adiabatic flow, but such formulae are complicated, and the error
occasioned by the assumption that the gas density remains constant
throughout the flow may be considered negjigible when only such pressure
differences are involved as occur in ordinary heating and ventilating
practice.
In the development of the formulae, diagrams, and tables for the flow
of air, use is made of the following basic equation for the flow of fluids :
If Hv be the velocity head in feet of a fluid, and the velocity, V, be expressed in feet
per minute, the fundamental equation is
V = 60 2g H
The factor g is the acceleration due to gravity, or 32.16 ft per second per second.
It is usual to express the head in inches of water for ventilating work and, since the
heads are inversely proportional to the densities of the fluids,
#v = 62.4
/Zy p
12
or
Hv = 5.2 -^
9
therefore,
V = 1096.5 .J^X__ (1)
I p
where
V — velocity in feet per minute.
hv = velocity head or pressure in inches of water.
p = weight of air in pounds per cubic foot.
For standard air (70 F and 29.92 in. barometer) p = 0.07495 Ib per cubic foot. Sub-
stituting this value in Equation 1 :
-5 V ocfe-* • ^ V
1096-5 ^^9* = 4005 V Av (2)
325
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
70
Llffl ILADMS fH PtHCEMT Of PlPE
FIG. 1. CURVE SHOWING Loss OF PRESSURE IN* ROUND ELBOWS
The drop In pressure in air distributing systems is due to the dynamic
losses and the friction losses. The friction losses are those due to the
friction of the air against the sides of the duct. The dynamic losses are
those due to the change in the direction or in the velocity of air flow.
Dynamic Losses
Dynamic losses occur principally at the entrance to the piping, in the
elbows, and wherever a change in velocity occurs. The entrance loss Is
the difference between the actual pressure required to produce flow and
the pressure corresponding to the flow produced; it may vary from 0.1 to
I'
tOO t5O ZOO . 2SO
-LME &ADW3 M PE&CZNT Of PfPE WlDTtt
FIG. 2. CURVE SHOWING Loss OF PRESSURE IN SQUARE ELBOWS
326
CHAPTER 20 — AIR DUCT DESIGN
0.5 times the velocity head. The pressure loss in elbows must also be
allowed for in the design. It is customary to express dynamic losses in
terms of the percentage of the velocity head; in other words, the per-
centage of that pressure corresponding to the average velocity in the duct
which is expressed in terms of inches of water gage. Figs. 1 and 2 show
the effect of changing the radius of elbows of square and rectangular
section. These charts are based on tests of pipe elbows of ordinary good
sheet metal construction. For example, a five-piece round pipe elbow
having a centerline radius of one diameter has a loss of about 25 per cent
of the velocity head. At a velocity of 2000 fpm the corresponding head
is 0.25 in, water gage, and at this velocity the elbow just referred to would
cause a pressure drop .of 0.063 in. water gage. Experience has shown that
good results may be obtained when the radius to the center of the elbow
is 1J^ times the pipe diameter. The pressure drop will then be approxi-
mately 17 per cent of the velocity head for round ducts, and 9 per cent
for square ducts. Very little advantage is gained in making elbows with
a radius of more than two diameters.
Friction Losses
Friction losses vary directly as the length of the duct, directly as the
square of the velocity, and inversely as the diameter. Since length is a
fixed quantity for any system, the factors subject to modification are the
area and the velocity, which determine the relation between the first cost
of the duct system and the cost of the power for overcoming friction.
The friction between the moving air and pipe surface causes a loss of
head which is numerically equal to the pressure required to maintain a
given velocity, and is expressed in the following modification of Fanning's
formula:
For round pipe and standard air (70 F and 29.92 in. barometer)
For rectangular ducts
where
JtL — loss of head, inches of water.
(V \2
— — — i = velocity head, inches of water.
4IX/O /
V = velocity of air, feet per minute.
L — length of pipe 1
D = diameter of pipe \ all in feet.
a, b — sides of rectangular duct J
/ = coefficient of friction.
C =— = length of pipe in diameters for one head loss.
For all practical purposes C vaiies only with the nature of the pipe
surface: C = 60 for perfectly smooth pipe; = 55 for pipe as used in planning
mill exhaust systems; = 50 for heating and ventilating ducts; = 45 for
327
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
SOO 000
600 ooo
500000
400 WO
500000
2000QO
ISO
100
Friction In Inches of Waterper 100 Ft,
FIG. 3. FRICTION OF Am IN PIPES
328
CHAPTER 20 — AIR DUCT DESIGN
smooth and 40 for rough conduits of tile, brick or concrete. However,
Fritzsche states (and numerous tests check very closely) that / varies
inversely as the 2/7 power of the pipe diameter, and inversely as the 1/7
power of the velocity, or inversely as the 1/7 power of capacity, which is
the same thing. Thus Formula 3 may be revised as follows, based upon a
loss of one velocity head (at 2000 fpm) in a length equal to 50 diameters
of 24-in. galvanized swedged pipe:
L ( V \13/7
The preceding formulae are based on standard air, and for other con-
ditions the friction varies directly as the air density and inversely (ap-
proximately) as the absolute temperature. The increase of friction due
to increase of air viscosity with increased temperature is small and is
generally neglected.
Friction Loss Chart
Fig. 3 is a convenient chart for determining the friction loss for various
air quantities in ducts of different sizes. The general form of this chart is
familiar, but it should be noted that it is corrected for changes in
the coefficient of friction based on the rule that the coefficient of friction
varies inversely as the 2/7 power of the diameter, and inversely as the
1/7 power of the velocity. Fig. 3 is based on a loss of one velocity head
(at a velocity of 2000 fpm) in a length equal to 50 diameters of 24-in.
round galvanized-iron duct of the usual construction. Although this
chart is laid out for a value of C equivalent to 50, it may be used for other
values of C by varying the friction inversely as this constant. For ex-
ample, if a rougher pipe is used with 40 as the value of C, the friction loss
as read from the chart should be multiplied by j^.
Example 1. Assume that it is desired to pass 10,000 cfm of air through 75 ft of 24-in.
diameter pipe. Find 10,000 cfm on the right scale of Fig. 3 and move horizontally left to
the diagonal line marked 24-in. The other intersecting diagonal shows that the velocity
in the pipe is 3200 fpm. Directly below the intersection it is found that the friction per
100 ft is 0.59 in.; then for 75 ft the friction will be 0.75 X 0.59 = 0.44 in. In a like man-
ner any two variables may be determined by the intersection of the lines representing
the other two variables.
Proportioning the Losses
Other losses of pressure occur at the entrance to the duct, through the
heating units, and at the air washer. In ordinary practice in ventilation
work it is usual to keep the sum of the duct losses M to 3^ &n<i the loss
through the heating units at less than J^ of the static pressure. The
remainder is then available for producing velocity. In the design of an
ideal duct system, all factors should be taken into consideration and the
air velocities proportioned so that the resistance will be practically equal
in all ducts regardless of length.
DUCT SIZES
The sizes of ducts and flues for gravity or mechanical circulation of air
are usually based on the losses due to friction, and these losses must be
kept within the available pressure difference. This pressure difference in
329
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
CHAPTER 20 — AIR DUCT DESIGN
mechanical ventilation is that derived from the fan, while in gravity
ventilation the aspirating effect due to the temperature and height of the
column of heated air causes the pressure difference.
Genera! Rules
The general rules to be followed in the design of a duct system are:
1. The air should be conveyed as directly as possible at reasonable velocities to obtain
the results desired with greatest economy of power, material and space.
2. Sharp elbows and bends should be avoided.
3. The sides of all ducts or flues should be as nearly equal as possible. (In no case
should the ratio between long and short sides be greater than 10 to 1.)
Procedure for Duct Design
The general procedure for designing a duct system is as follows:
1. Study the plan of the building and draw in roughly the most convenient system of
ducts, taking cognizance of the building construction, avoiding all obstructions in steel
work and equipment, and at the same time maintaining a simple design.
2. Arrange the positions of duct outlets to insure the proper distribution of heat.
3. Divide the building into zones and proportion the volume of air necessary to
supply the heat for each zone.
4. Determine the size of each outlet, based on the volume as obtained in the preceding
paragraph, for the proper outlet velocity.
5. Calculate the sizes of all main and branch ducts by either of the following two
methods:
a. Velocity Method. Arbitrarily fix the velocity in the various sections, reducing the
velocity from the point of leaving the fan to the point of discharge to the room. In
this case the pressure loss of each section of the duct is calculated separately and
the total loss found by adding together the losses of the various sections.
b. Friction Pressure Loss Method. Proportion the duct for equal friction pressure
loss per foot of length.
6. Calculate the friction for the duct offering the greatest resistance to the flow of
air, which resistance represents the static pressure which must be maintained in the fan
outlet or in the plenum space to insure distribution of air in the duct system. The duct
having the greatest resistance will usually be that having the longest run, although not
necessarily so.
Air Velocities
The following velocities of air are considered standard for public
buildings:
1. Through the outside air intakes, 1000 fpm,
2. Through connections to and from heating unit, 1000 to 1200 fpm.
3. Through the main discharge duct, from 1200 to 1600 fpm.
4. In branch ducts, 600 to 1000, and in vertical flues, 400 to 800 fpm.
5. In registers or grilles, 200 to 400 fpm depending upon the size and location. If
diff users of proper design are used, 25 per cent higher air velocities are permissible.
These duct velocities may safely be increased 20 per cent if first-class
construction is used to prevent any breathing, buckling, or vibration.
High velocities "at one point in the system neutralize the effect of proper
design at all other points; hence the importance of splitters in elbows and
similar precautions. For industrial buildings noise is seldom considered,
and main duct velocities as high as 2800 or 3000 fpm may be used where
conditions will permit. For department stores and similar buildings,
331
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
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CHAPTER 20 — AIR DUCT DESIGN
maximum velocities with good construction and design may be as high
as 2000 or 2200 fpm in main ducts, with suitable reduction in branches
and outlets. With these velocities first-class duct construction is essential.
Proportioning the Size for Friction
By means of Figs. 4 and 5 the diameter of branch pipes necessary to
carry a given percentage of the total air in the main pipe and to maintain
equal friction per foot of the length through the entire system may be
determined. These charts, as well as Fig. 3, are based on the assumption
that the coefficient of friction varies inversely as the 1/7 power of the
capacity.
Example 2. Suppose a 60-in. main pipe is to be used, and it is desired to know the
size of branch pipe required to carry 50 per cent of the total air in the main. Find 50
per cent at the left of the chart, move right to the 60-in. diagonal line and note directly
above at the top of the chart that the branch pipe will be 46.5 in. in diameter.
Where rectangular ducts are used it is frequently desirable to know the
equivalent diameter of round pipe to carry the same capacity and have
the same friction per foot of length. Table 1 gives directly the circular
equivalent of rectangular ducts for equal friction and capacity. To
obtain the size of rectangular ducts for different capacities, but of the
same friction per foot of length, first obtain the equivalent round pipe for
equal friction. Thus, if a branch of sufficient size to carry 30 per cent of
a 12 x 36-in. pipe is desired, it is found from Table 1 that the main is
equivalent to a 22.2-in. diameter round pipe. From Fig. 5, 30 per cent of
this is a pipe 14.3 in. in diameter, and referring again to Table 1, the
rectangular equivalent branch is a 12 x 14-in., 10 x 17J^-in., or any other
desirable combination.
Multiplying or dividing the length of each side of a pipe by a constant
is the same as multiplying or dividing the equivalent round size by the
same constant. Thus, if the circular equivalent of an 80 x 24-in. duct is
required, it will be just twice that of a 40 x 12-in. duct, or 2 X 23.3 =
46.6 in.
DUCTS FOR PUBLIC BUILDINGS
A main duct with branches is generally used to convey tempered air
for ventilation purposes only. In place of individual ducts, a compara-
tively large main duct supplies air by branches to the room or rooms. The
velocities vary according to the nature of the installation and the degree of
quietness required. At the start of the run a velocity as high as 2000 fpm
may be used, but this is considered the maximum for public building
work, and is reduced to from 400 to 800 fpm in the risers. This duct system
may be designed so that the loss of pressure in the branches is equalized in
a manner similar to that previously described.
Equal Friction Method
Example S. Fig. 6 shows a typical layout of an air distribution 'system which is
applicable for ventilation of hotel dining rooms and offices.
The volume of air in cubic feet per minute for the room is determined on the basis of
the number of air changes per hour required. In the example shown, the room ventilated
is a hotel diningf room 135 ft x 85 ft x 15 ft. A 7J4-minute air change (8 air changes per
hour) is assumed for proper ventilation, giving 22,935 cfm as the air required.
22 935
The clear area of the fresh air inlet is based on a velocity of 1000 fpm or ^ =
333
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AMERICAN SOCIETY of HEATING dnd VENTILATING ENGINEERS GUIDE, 1935
336
CHAPTER 20 — AIR DUCT DESIGN
22.94 sq ft. If the air washer is provided with automatic humidity control, the tempering
coil should raise the temperature of the entering air to 32 F. The washer with its auto-
matic control will then raise the temperature from 32 F to 42 F. If the washer is not
provided with automatic humidity control, the tempering coil must raise the temperature
of the entering air to at least 55 F to allow for some temperature drop in the washer due
to evaporation. The reheating coil is selected to raise the temperature of the air from
that leaving the air washer to 70 F. The air washer should have a maximum velocity of
500 fpm through the clear area, which, in this case, is 46 sq ft. For more detailed infor-
mation on tempering coil and air washer control, see Chapters 23 and 14.
Since the plan shows a moderately short run of main duct with no risers near the fan
outlet, a fan should be selected which will have the required capacity of 22,935 cfm with
a maximum velocity through the fan outlet of 1400 fpm. The outlet area, therefore,
should be 16J^ sq ft.
TABLE 2. PIPE SIZES FOR EXAMPLE 3a
VOLUME
OF AlH
(CFM)
PEE CENT
o? TOTAL
| VOLUME
DIAMETER or
PIPH
( (INCHES)
EQUIVALENT SIZE OF
RECTANGULAR DUCT
(INCHES)
22,935
1 100.0
J 56 ! 60x44
12,510
; 54.6
45 ; 58 x 30
10,425
45.4
« 42
50x30
8,340
' 36.3
! 39
42x30
6,255
! 27.2
35
42x24
4,170
i 18.2
291A ', 30x24
2,085
9.1
23
30x15
I
[
a Velocity through diffusers (not shown) to be approximately 300 fpm.
The main pipe size should be selected to give a velocity equal to or less than the
velocity at the fan outlet. Choosing a 56-in. pipe with a cross-sectional area of 17.1 sq ft,
the velocity in the main pipe will be 1340 fpm. Using the friction pressure loss method
this 56-in. main pipe will be taken as the basis of calculation.
Fig. 6 shows the amount of air to be handled by each section of pipe. Expressing the
volume handled by each section as a percentage of the total volume and using the charts,
Figs. 4 and 5, the pipe sizes are as shown in Table 2.
The pressure at the outlets nearest the fan will be greater than at the pipes farther
along the run so that the former will tend to deliver more than the calculated amount of
air. To remedy this condition, volume regulating dampers should be located at the base
of each riser and adjusted for proper distribution. At points where branches leave the
main it may be advisable, depending upon the nature of the installation, to install
adjustable splitters similar to that shown in Fig. 6 where the main duct divides into the
58 in. X 30 in. and 50 in. X 30 in. branches.
The rectangular equivalents are selected from Table 1 ; the width to depth proportion
will be determined by construction requirements and ease of fabrication. The calcu-
lation of the friction is as follows:
The longest run from the fan outlet to diffuser is 150 ft 0 in.; 150 ft of 56-in. pipe is
. , . . 150 X 12 ooo,ra
equivalent to - rr — - ___________________________________ — .................................................. ~6£»& dia.
*K)
Two 45-in., 90-deg elbows (2 X g| X 10) ____________ . ......................... ------- . ................ 16.1 dia.
OQ
Two 23-in., 90-deg elbows (2 X gg X 10)— ............... ..._ ....................................... 8.2 dia.
23
Two 23-in., 90-deg elbows in riser (2 X ^ X 30) ............................................. —. 24.7 dia.
(Two bad elbows in riser, each equivalent to 30 diameters of duct).
Total diameter of 56-in. pipe _______________________ .................................................. 81.2
337
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
/1340\2
The velocity head corresponding to a velocity of 1340 fpm is ( TQ/VF ) = 0.112 in.
81 2
Taking 50 diameters as one head loss, then ' X 0.112 = 0.182 in. static loss in duct.
ou
Where the connection pieces are made with long easy slopes and the general work-
manship is good, a regain in static pressure may be deducted from the foregoing pressure
loss. This can be taken as approximately two-third? the difference in velocity pressures
at the fan outlet and the last run of pipe. The velocity in the riser is 667 fpm with a
corresponding velocity pressure of 0,033 in. The fan outlet velocity is 1400 fpm with
a corresponding velocity pressure of 0.122 in. The regain equals % (0.122 — 0.033)
= 0.059 in.
The net static pressure loss in the duct only is then :
0.182 in. - 0.059 in
..0.123 in.
Other friction losses are as follows:
(1) Fresh air intake 1000-fpm velocity (11A heads X 0.0625) 0.094 in.
(2) Tempering coil loss (from manufacturer's tables) 0.100 in.
(3) Air washer loss (from manufacturer's tables)... 0.250 in.
(4) Reheating coil loss (from manufacturer's tables)... 0.100 in.
(5) Allowance for regulating dampers and diffusers 0.100 in.
Static pressure loss of system 0.767 in.
The fan should be selected from the manufacturer's ratings which, according to the
Standard Test Code for Disc and Propeller Fans, Centrifugal Fans and Blowers1, will
deliver 22,935 cfm at a static pressure of 0.767 in. and which has an outlet area of 16H
sqft.
The method of design used in Example 3 is the equal friction method
described under the heading Procedure for Duct Design. This involves
the arbitrary reduction of velocity from the fan outlet to the point of
discharge to the room, and the friction is calculated by adding the pressure
losses of each section of duct. This method requires dampering in the
risers.
Example 4- Fig. 7 shows an exhaust system layout for exhausting from buildings of
the same type as in Example 3, Assume the air requirements based on the number of
air changes per hour to be 16,800 cfm. Using a velocity of 1400 fpm in the main duct at
TABLE 3. PIPE SIZES FOR EXAMPLE 4a
VOLUME
or Am
(CFM)
PEE CENT
OF TOTAL
VOLUME
DIAMETER OF
PIPE
(INCHES)
EQUIVALENT SIZE OF
RECTANGULAR DUCT
(INCHES)
16,800
100.0
47
38x48
11,550
68.8
41
30x46
9,450
56.2
38
30x40
5,250
31.3
31
24x34
4,200
25.0
28.5
24x28
3,150
18.8
25.3
16x34
2,100
12.5
21.6
16x24
a Velocity through intake grilles (not shown) to be approximately 400 fpm.
*See Chapters 17 and 41.
338
CHAPTER 20 — AIR DUCT DESIGN
FIG. 7. EXHAUST SYSTEM LAYOUT
the fan inlet, which Is an average velocity for this type of system, the area of the main is
12 sq ft, which corresponds to a 47-in. pipe. Referring to Example 3, and using the
charts, Figs. 4 and 5, the pipe sizes are as indicated in Table 3.
All risers will require dampering as in Example 3. The calculation of the friction
is as follows:
The longest run from the intake grille to fan inlet is 100 ft.
(TOO ^ 12\
-yj J 25.6 dia.
Two 28^-in., 90-deg elbows in riser (12<28*X80^ 36 4 dia
(Two bad elbows in riser each equivalent to 30 diameters of duct).
/ *?S f\ \f "\(Jf\
One 28H-in., 90-deg elbow in horizontal run ^ ' 4? J 6.0 dia.
Total diameter of 47-in. pipe — - 68-0 dia.
(1400\2
|OQg \ = 122 in.
AS "^ fl 1 04?
Taking 50 diameters as one head loss, then ^ ' - 0.166 in.
(2) Intake loss from griU^(lK heads at a 400 fpm velocity IK X 0.01) 0.015 in.
(3) Static pressure required to produce one velocity head at 1400 fpm — 0.122 in.
(4) Loss occasioned by step-up of velocity (0.20 X 0.122) _ 0.024 in.
(Ibis loss varies from 0.05 to 0.40 velocity bead depending upon tne nature of the change.
Far average systems 0.20 velocity head is a dose approximation.)
Static pressure loss on inlet side, . 0-327 in.
339
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
FIG. 8. ISOMETRIC VIEW OFDucx
SHOWING LOCATION OF STIFFENING
SEAMS ON TOP AND SIDE PANELS
OF DUCT
THESE CROSSBREAKS
"ARE NEVER
SHOWN OM A PLAN
SECTION
r
MEET
ELEVATION
REINFORCED
CROSS SEAMS
SEAMS BETWEEN ADJACENT
PANELS OR PLAIN CROSS SEAMS
FIG. 10. METHOD. OF INSTALLING
HEATING UNIT
FIG. 9. DETAILS OF SEAMS
FIG. 12. FAN DISCHARGE CONNECTION
FIG, 11. INSTALLATION OF EASEMENT
IN DUCT AROUND OBSTRUCTION
340
CHAPTER 20 — AIR DUCT DESIGN
To this must be added the resistance on the discharge side of the fan. A fan outlet
velocity of approximately 1500 to 1000 fpm may be used. Assuming the fan outlet to
be equivalent in area to a 45-in. pipe, the velocity is 1525 fpm.
Loss on discharge (15 ft from fan outlet to discharge):
15 X 12 ...
— — = 4 diameters of 4o-m. pipe.
'iO
The velocity head corresponding to a velocity of 1525 fpm is 0.145 and the discharge-
side loss is — — gg = 0.012 in. The total static pressure loss of the system is then:
0.012 -j- 0.327 = 0.339 in.
The fan will be selected to handle 16,800 cfm at a static pressure of 0.339 in. and
to have an outlet velocity of 1525 fpm. Outlet area 11 sq ft.
Where there are one or more ducts with branches, the velocity of air in
the ducts may be either chosen arbitrarily or calculated for friction losses.
When arbitrary values are assigned, a certain amount of dampering
should be provided for; this will be small when the method chosen permits
a drop in velocity as the quantity of air is reduced.
After the total air quantity and the size of fan are ascertained, the main
duct is usually fixed as being at least equal in area to the fan outlet, or
perhaps 10 per cent greater. From this main pipe all others are propor-
tioned. For example, if the main duct is 30 in. in diameter, a branch to
carry 10 per cent of the total capacity should be 12.7 in. in diameter (see
Fig. 4) in order to have the same friction per foot of length, while one
carrying one-half the total capacity of a 30-in. main with the same friction
loss per foot would be 23.4 in. in diameter. By this method of equalizing
friction it is unnecessary to consider the resistance of each section of pipe
independently, but only to know the distance from the fan outlet to the
end of the longest run of pipe, the number and size of elbows, and the
diameter and velocity in the largest pipe.
Example 5. If the greatest length of piping in a system is 130 ft with a 26-in. diameter
main pipe and one 20-in. elbow, the piping having been designed for equal friction per
foot of length, the friction would be the same as for 130 linear feet of 26-in. pipe, or
60 diameters. To this should be added the friction loss in elbows, in this case one 20-in.
elbow, which has a loss equivalent to one-fifth of a velocity head or ten diameters of
20
20-in. pipe. This in turn is -^ X 10 = 7.7 diameters of 26-in. pipe. The total equivalent
length of the system will then be 60 -f- 7.7, or 67.7 diameters. Since 50 diameters is
f\7 7
equivalent to one velocity head, the loss is ' = 1.35 times the velocity head. If
ou
the velocity is, for example, 2200 fpm, corresponding to 0.3-in. pressure, the friction loss
of the system will be 1.35 X 0.3 = 0.405 in.
Frequently the prevention of sound in a heating or ventilating system
imposes more severe restrictions than the prevention of excessive pressure
drop. This question is highly involved and requires consideration of
many factors. The air velocities to be used will vary with the standard of
construction used in the ducts themselves as well as with the nature of the
occupancy and the construction of the building. In general, architects
and engineers who leave the details of duct construction to the contractor
must, of necessity, design for lower velocities than might be required for
quiet operation if proper construction details were always followed. The
341
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
ROSETTE
FIG. 13. AIR SPLITTERS
INSTALLED IN ELBOW
VANES
FIG. 14. AIR SPLITTERS IN-
STALLED IN ELBOW AT FAN
DISCHARGE
FIG. 15. AIR SPLITTERS
IN BRANCH DUCTS AND
ELBOWS
contractor may be expected to build the ducts by the least expensive
methods, and the engineer must anticipate this. For further information
on noise reduction, see Chapter 18.
Details of Duct Construction
If panel construction is used with standing seams or similar reinforce-
ment, and the panels are cross-broken to give rigidity, there is less like-
lihood of vibration due to air flow, or deflection due to air pressure.
Elbows made without splitters, and improperly shaped transformation
sections produce high local velocities which are the cause of noise in duct
work. The use of first-class duct construction with well-designed trans-
formation sections and splitters in elbows tends to maintain relatively
uniform velocities with decrease in turbulence and in the noise produced.
Figs. 8 to 15 show acceptable construction details for rectangular
ducts, elbows, transformation pieces or connections, and air splitters.
Other methods are also acceptable, such as the use of angle iron stiffeners
for large ducts. Good construction is essential to the elimination of duct
noises and for the prevention of a flimsy installation.
Fig. 8 is an isometric view of a duct showing the location of the
stiffening seams on the top and side panels. The cross seams should not
occur at the same place but should be staggered as indicated. Heating
units should be installed as shown in Fig. 10 with the duct connections
making an angle of not less than 45 deg, but preferably 60 deg. Fan dis-
TABLE 4. SHEET METAL GAGES FOR RECTANGULAR DUCT CONSTRUCTION2-
GA&B
WIDTH or DUCT
SEAM
RTOWORCBD SEAM
26
Up to 12 in.
24
13 in. to 30 in.
1
22
31 in. to 48 in.
1
22
49 in. to 60 in.
1M
J^ in. x 1% in.
20
61 in. to 90 in.
ii4
Min.xlJiin.
« If panels are not cross-broken two gages heavier material should be used.
342
CHAPTER 20 — AIR DUCT DESIGN
charge connections should have a maximum slope of 1 in 7, as indicated in
Fig. 12. Whenever a pipe or other obstruction passes through a duct
an easement should be placed around the pipe as indicated in Fig. 11.
Air splitters should be installed in elbows as shown in Figs. 13 and 14.
The recommended gages for rectangular sheet metal duct construction are
given in Table 4.
REFERENCES
Fan Engineering, Buffalo Forge Co.
Heat Power Engineering by Barnard, Ellenwood, and Hirshfeld, Part III.
Mechanical Engineers' Handbook by Lionel S. Marks, McGraw-Hill Book Co.
The Flow of Liquids, by W. H. McAdams, Refrigerating Engineering, February, 1925, p. 279.
A Study of the Data on the Flow of Fluids in Pipes, by Emory Jvemler, A.S.M.E. Transactions, Hy-
draulics Section, August, 31, 1933, p. 7.
PROBLEMS IN PRACTICE
1 • Why is it desirable to make elbows with a radius equal to one and one-half
times the pipe diameter?
Reference to Figs. 1 and 2 will show that while the loss of velocity head, as indicated by
the curves, shows considerable variation for elbows between the range of 50 and 150 per
cent radius, the line is practically straight after 150 per cent, indicating very little
variation in loss of head for elbows of larger radius.
2 • What is the best shape to use for duets?
The shapes to be used in designing ducts, in the order of their preference, are round,
square, and rectangular.
3 • What determines which shape to use?
Structural and space conditions. Because ducts are as a rule part of the building or
structure, it is necessary to proportion their sizes to fit the spaces available.
4 • What is meant by "arbitrarily fix the velocity in the various sections?"
When using the vejocity method as a basis for design, the maximum allowable velocity
is fixed for the main supply duct at the fan, and this velocity is gradually decreased as
each branch or outlet is taken off the main supply duct.
5 • Which system of duct design is to be preferred, the velocity method or the
friction pressure loss method?
The friction pressure loss method can be used to advantage where no structural or
building conditions limit the shape of the ducts. Where these limiting conditions exist
the velocity method is to be preferred.
6 • Are the grille sizes figured on the same basis as the outlets?
The free area through the grilles is figured the same as the outlets, and this area is
increased from 20 to 50 per cent, depending on the design of the grille, to allow for the
loss of area caused by the construction of the face of the grille,
7 • Where it is necessary to provide steel angle braces, how far apart should
they he spaced?
Angle braces for large ducts should be placed on 3-ft 0-in. centers.
343
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
8 • How much air will a 10-in. by 24-in. duct handle if it is part of a system
designed on a pressure drop of 0.1 in. per 100 feet of run?
1450 cfm ( Table 1 and Fig, 3j.
9 • How does a splitter at a duct junction influence the volume of the air going
through each branch?
A splitter facing the direction of air flow cuts off the air and delivers the desired amount
to the branch.
10 • Why does a wide, shallow duct offer more resistance to the now of ah* than
does a square duct of equal cross-sectional area?
The perimeter of the wide, flat duct is greater than that of the square-section duct, so the
former has the greater frictional area which increases the resistance and thus reduces the
volume at any given pressure.
11 • What methods are used to keep large ducts from vibrating because of air
pulsations, and from sagging because of their own weight?
External bracing, such as standing seams, or structural shapes, like tees or angles, should
be placed across the top and bottom. Exterior braces or cross buckling of metal sheets
in diagonal panels may be used for the sides of large ducts.
12 • What velocities of air flow should be used in the trunk ducts of a venti-
lating system in a public building?
From 1200 to 1600 fpm.
13 • In a ventilating system in a residence, what is the recommended air
velocity through supply registers and grilles?
400 fpm.
344
Chapter 21
E\T»USTRIAl, EXHAUST SYSTEMS
Types, Design of Systems, Suction and Velocity Requirements,
Design of Hoods, Design of Duct Systems, Collectors, Resistance of
Systems, Selection of Fans and Motors
T7 XHAUST and collecting systems are found in almost every industry
F^ and are a vital adjunct in maintaining safe and hygienic conditions1.
The present chapter attempts to give general information relating to the
design of factory exhaust systems in order that efficient and economical
control of dusts and fumes may be achieved.
TYPES OF SYSTEMS
There are two general arrangements, the central and the group systems.
In the central system a single or double fan is located near the center of
the shop with a piping system radiating to the various machines to be
served. In the group system, which is sometimes employed where the
machines to be served are widely scattered, small individual exhaust fans
are located at the center of the machine groups. The group arrangement
has the advantage of flexibility.
Exhaust systems are also classified by the means employed to collect
dust or other material handled. The dust or refuse may be collected and
controlled by enclosing hoods, open hoods, inward air leakage, or by
exhausting the general air of the room.
With some classes of machinery it is not feasible to closely hood the
machines and in these cases open hoods over or adjacent to the machines
are provided to collect as much as possible of the dust and fumes. This
class includes such machines as rubber mills, package filling machinery,
sand blast, crushers, forges, pickling tanks, melting furnaces, and the
unloading points of various types of conveyors.
The open hoods should be placed as close to the source of dust or fumes
as possible, with due regard to the movements of the operator. When the
hood must be placed at some distance above the machine it should be
large enough to encompass an area of considerable extent as diffusion is
usually quite rapid.
Consideration must also be given to the natural movement of the
fumes. For those that are lighter than air the hood should be over or
above the machine and where a heavy vapor or dust-laden air at ordinary
temperature is to be removed, horizontal or floor connections are required.
If it is attempted to remove heavy dust such as lead oxides by an over-
head hood the conditions may be worse than if no exhaust were used at
Criteria for Industrial Exhaust Systems, by J. J. Bloomfield (A.S.H.V.E. Journal Section, Heating,
Piping and Air Conditioning, July, 1934).
345
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
all, owing to the rising air current carrying the dust up through the
breathing zones. The objective to keep in mind in all cases is to take
advantage of the natural tendency of the material to move upward or
downward.
In another class of operation the main objective is to prevent the escape
of dust into the surrounding atmosphere, the removal of some dust from
the machine or enclosure being merely incidental. The dust-creating
apparatus is enclosed within a housing which is made as tight^ as prac-
ticable, and sufficient suction is applied to the enclosure to maintain an
inward air leakage, thus preventing escape of the dust. While the exhaust
system is required to handle only the air which leaks in _ through the
crevices and openings in the enclosure, yet in many installations leakages
are very high and great care is required to obtain satisfactory results
with a system of this kind. The inward-leakage principle is utilized for
controlling dust in the operating of tumbling barrels, grinding, screening,
elevating, and similar processes.
Certain dust and fume producing operations are best carried on by
isolating the process in a separate compartment or room and then apply-
ing general ventilation to this space. The compartment or room in which
the work is performed should be as small as is consistent with convenience
in handling the work. The ventilating system should be designed so
that a strong current of clean air is drawn across the operator, and away
from him toward the work, where the dust is picked up and carried
from the room.
DESIGN OF SYSTEMS
The first step in the design of an exhaust system is to determine the
number and size of the hoods and their connections. No general rules,
however, can be given since hood and duct dimensions are determined by
the characteristics of the operations to which they are applied. When a
tentative decision regarding the set-up has been made, it is then necessary
to obtain the suction and air velocities required to effect control. At this
point the designer must rely upon the prevailing practice and on such
physical data relating to hoods, duct systems and collectors as are avail-
able. Finally, in choosing the fan, the area of the intake should be equal
to or greater than the sum of the areas of the branch ducts. The speed, of
course, must be sufficient to maintain the estimated suction and air
velocities in the system. In general, the most important requirements of
an efficient exhaust and collecting system are as follows2 :
1. Hoods, ducts, fans and collectors should be of adequate size.
2. The air velocities should be sufficient to control and convey the materials collected.
3. The hoods and ducts should not interfere with the operation of a machine or any
working part.
4. The system should do the required work with a minimum power consumption.
5. When inflammable dusts and fumes are conveyed, the piping should be provided
with an automatic damper in passing through a fire-wall.
6. Ducts and all metal parts should be grounded to reduce the danger of dust ex-
plosions by static electricity.
7. The design of an exhaust system should afford easy access to parts for inspection
and care.
2For more detailed requirements see Safe Practice Pamphlets Nos, 32 and 37, published by thtNaifonel
Safety Council, Chicago.
346
CHAPTER 21 — INDUSTRIAL EXHAUST SYSTEMS
SUCTION AND VELOCITY REQUIREMENTS
The removal of dust or waste by means of an exhaust hood requires a
movement of air at the point of origin sufficient to carry It to a col-
lecting system. The air velocities necessary to accomplish this depend
upon the physical properties of the material to be eliminated and the
TABLE 1. SIZE OF CONNECTIONS FOR WOOD- WORKING MACHINERY
TYPE OF MACHINE
DIAMETER OF
CONNECTIONS IN
INCHES
Circular saws, 12-in. diam — ; 4
Circular saws, 12-24-in. diam I 5
Circular saws, 24-40-in. diam ; 6
Band saws, blade under 2 in. wide._ 4
Band saws, blade 2-3 in. wide._ „ 5
Band saws, blade 3-4 in. wide j 6
Band saws, blade 4-5 in. wide J 7
Band saws, blade 5-6 in. wide._ ' 8
Small mortisers j 6
Single end tenoners „ j 6
Double end tenoners _ ! 7
Double end, double head tenoners _ „ 10
Planers, matchers, moulders, stickers, jointers, etc. —
With knives, 6-10 in „ 5-6
With knives, 10-20 in 6-8
With knives, 20-30 in .__ „ „ 6-10
Shapers, light work j 4—5
Shapers, heavy work _ j 8
Belt sander, belt less than 6 in. wide._ 5
Belt sander, belt 6-10 in. wide „ 6
Belt sander, belt 10-14 in. wide I 7
Drum sander, 24 in „ 5
Drum sander, 30 in. _ „ 6
Drum sander, 36 in , 7
Drum sander, 48 in. 8
Drum sander, over 48 in 10
Disc sander, 24 in. diam. 5
Disc sander, 26-36 in. diam. . 6
Disc sander, 36-48 in, diam 7
Arm sander _ _ 4
direction and speed with which it is thrown off. If the dust to be removed
is already in motion, as is the case with high-speed grinding wheels, the
hood should be installed in the path of the particles so that a minimum
air volume may be used effectively. It is always desirable to design and
locate a hood so that the volume of air necessary to produce results is as
small as possible.
The static suction at the throat of a hood is frequently used in practice
as a measure of the effectiveness of control* This is of considerable value
where exhaust systems adapted to particular operations have been
standardized by practice. Tables 1 and 2 present the duct sizes usually
employed for standard wood-working machinery and for grinding and
buffing wheels. Static pressures which in practice have been found
necessary to control and convey various materials, are given in Table 3.
It must be remembered, however, that the suction is merely a rough
347
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 2. SIZE OF CONNECTIONS FOR GRINDING AND BUFFING WHEELS
MAX.
MlN. DlAM.
DIAMETER <
3F WHEELS
GRINDING
SURFACE
OF BRANCH
PIPES IN
SQ IN.
INCHES
Grinding —
6 in. or less, not over 1
in. thick.
19
3
7 in. to 9 in. inclusive
, not over IJ'
^ in. thick
43
10 in. to 16 in, *
u u 2
in. a
101
4
17 in. to 19 in. "
a « 3
in. "
180
4J^
20 in. to 24 in. a
* « 4
in. « ._..
302
5
25 in. to 30 in. a
« u 5
in. a _„
472
6
Buffing —
6 in. or less, not over 1
in. thick.
19
3V*>
7 in. to 12 in. inclusive
, not over IJ/
^ in. thick
57
4
13 in. to 16 in. "
a « 2
in. " ..„„
101
4J^
17 in. to 20 in.
a « 3
in. u
189
5
21 in. to 27 in. «
« « 4
in. a
338
6
27 in. to 33 in. tf
« « 5
in. a
518
7
TABLE 3. SUCTION PRESSURES REQUIRED AT HOODS
STATIC SUCTION IN
INCHES OF WATER
Exhausting from grinding and buffing wheels
Exhausting from tumbling barrels
Exhausting from wood-working machinery — light duty
Exhausting from wood-working machinery — heavy duty
Shoe machinery exhaust
Exhausting from rubber manufacturing processes
Flint grinding exhaust .
Exhausting from pottery processes.....
Lead dust and fume exhaust
Fur and felt machinery exhaust--
Exhausting from textile machinery.
Exhausting from elevating and crushing machinery
Conveying bulky and heavy materials
2
2
2-4
2-3
2
2 '
2
2-4
2-3
2-3
2
3-5
measure of the air volume handled and consequently of the air velocity at
the opening of the hood. The elimination of any dusty condition requires
added information concerning the shape, size and location of the hood
used with regard to the operation in question.
In some states grinding, polishing and buffing wheels are subject to
regulation by codes. The static suction requirements, which range from
1^4 to 5 in. water displacement in a £/-tube, should be followed although
in several instances they may appear to be excessive. Frequently, in
these operations, a large part of the wheel must be exposed and the dust-
laden air within the hood is thrown outward by the centrifugal action of
the wheel, thus counteracting useful inward draft. This tendency may
be diminished by locating the connecting duct so as to create an air flow
of not less than 200 fpm about the lower rim of the wheel.
Exact determinations of hood control velocities are not available, but
348
CHAPTER 21 — INDUSTRIAL EXHAUST SYSTEMS
It is safe to assume that for most dusty operations they should not be less
than 200 fpm at the point of origin. For granite dust generated by
pneumatic devices, Hatch et al3 give velocities from 150 to 200 fpm,
depending on the type of hood used, as sufficient for safe control. Con-
sidering the character of the industry, air velocities of this order may be
extended to similar dusty operations. The method for approximately
determining these velocities in terms of the velocity at the hood opening
is given below.
DESIGN OF HOODS
No set rule can be given regarding the shape of a hood for a particular
operation, but it is well to remember that its essential function is to create
an adequate velocity distribution. The fact that the zone of greatest
effectiveness does not extend laterally from the edges of the opening may
frequently be utilized in estimating the size of hood required. Where
complete enclosure of a dusty operation is contemplated, it is desirable to
leave enough free space to equal the area of the connecting duct. Hoods
for grinding, polishing and buffing should fit closely, but at the same time
should provide an easy means for changing the wheels. It is advisable to
design these hoods with a removable hopper at the base to capture the
heavy dusts and articles dropped by the operator. Such provisions are of
assistance in keeping the ducts clear. Air volumes used to control many
dust discharges may often be reduced by effective baffling or partial
enclosure of an operation. This procedure is strongly urged where dusts
are directed beyond the zone of influence of the hood.
Axial Velocity Formula for Hoods
When the normal flow of air into a hood is unobstructed, the following
formula may be used to determine the air velocity at any point along the
axis:
100 - Y **
where
Y — per cent of velocity at opening.
A = area of opening, square inches (or square feet).
x = distance outward from opening, inches (or feet).
It is important to note that the velocity function varies in direct
proportion to the area. Hence, under certain conditions, a large opening
may function more effectively than a small one for the same volume of
flow. The formula, of course, presumes that the air velocity distribution
across the hood opening is uniform4.
Example 1. A small hood 64 sq in. in area handles 400 cfm. What will be the air
velocity at a point 5 in. outward along the axis if the flow is unobstructed?
*Hatch, Theodore, Drinker, Philip, and Choate, Sarah P., Control of the SiEcosis Hazard in the Hard
Rock Industries. I. A Laboratory Study of the Design of Dust Control Systems for Use with Pneumatic
Granite Cutting Tools. (Journal of Industrial Hygiene, VoL XII, No. 3, March, 1930).
^Velocity Characteristics of Hoods under Suction, by J. M. DaHaVaHe (A.S.H.V.E. TRANSACTIONS
Vol. 38, 1932).
349
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1035
Solution. Substitute in Equation 1 and solve for F, thus
Y 0.1 X 64
100 - F 5X5
from which Y — 20.4 per cent of the velocity at the opening of the hood.
400 X 144
Velocity at opening = ^ ~ 900 fpm
Hence, the velocity at the point in question is 900 X 0.204 = 184 fpm
Air Flow from Static Readings
The volume of air flow into any hood may be determined from the
following equation :
Q * 4005 fa V/zT (2)
where
Q — volume of air flow, cubic feet per minute.
& = area of connecting duct, square feet.
At = static suction at throat of hood, inches of water.
/ = orifice or restriction coefficient, which varies from 0.6 to 0.9 depending on the
shape of the hood.
An average value of /is 0.71, although for a well-shaped opening a value
of 0.8 may be used. If it is assumed that the entrance loss of a hood is
proportional to the velocity head, / can be determined by the relation:
where
the velocity head.
the entrance loss.
For duct ends and abrupt openings h^ = h? and for flared openings
&e - 0.5AV.
The term static suction is not a good measure of the effectiveness of a
hood unless the area of the opening and the location of the operation with
respect to the hood are known. This is clearly indicated by Equation 1
which shows that the velocity function at any point along the axis varies
directly as the area of the opening and inversely as the square of the
distance. However, this formula coupled with Equation 2 should serve
to indicate the velocity conditions to be expected when operations are
conducted external to the hood opening,
Large Open Hoods
Large hoods, such as are used for electroplating and pickling tanks,
should be subdivided so the area of the connecting duct is not less than
one-fifteenth of the open area of the hood. Frequently, it will be found
necessary to branch the main duct in order to obtain a uniform distri-
bution of flow. Canopy hoods should extend 6 in. laterally from the tank
for every 12-in. elevation. In most cases, hoods of this type take advan-
tage of the natural tendency of the vapors to rise, and air velocities may
be kept low. Cross drafts from open doors or windows disturb the rise of
350
CHAPTER 21 — INDUSTRIAL EXHAUST SYSTEMS'
the vapors and therefore provision must be made for them. The air
velocities required also depend upon the character of the vapors given off,
cyanide fumes, for example, requiring an air velocity of approximately
75 fpm on the surface of the tank and acid and steam vapors requiring
velocities as low as 25 to 50 fpm. The tota.1 volume of air flow necessary
to obtain these velocities may be approximately determined from the
following simple formula:
Q = 1.4PDV (4)
where
Q = total volume of air handled by hood, cfm.
P = perimeter of the tank, feet.
D = distance between tank and hood opening, feet.
V — air velocity desired along edges and surface of tank, fpm.
Spray Booths
In the design of an efficient spray booth, it is essential to maintain an
even distribution of air flow through the opening and about the object
being sprayed. While in many instances spraying operations can be
performed mechanically in wholly enclosed booths, the volatile vapors
may reach injurious or explosive concentrations. At all times the con-
centrations of these vapors, and particularly those containing benzol,
should be kept below 100 parts per million. Spray booth vapors are
dangerous to the health of the worker and care should be taken to mini-
mize exposure to them.
It is recommended in the design of spray booths that the exhaust duct
be located in a horizontal position slightly above the object sprayed.
Stagnant regions within the booth should be carefully avoided or should
be provided with a vertical exhaust. The air volume should be sufficient
to maintain a velocity of 150 to 200 fpm over the open area of the booth
and the vapors should be discharged through a suitable stack to permit
dilution5.
Hoods for Chemical Laboratories
Hoods used in chemical laboratories are generally provided with
sliding windows which permit positive control of the fumes and vapors
evolved by the apparatus. Their design should offer easy access for the
installation of chemical equipment and should be well lighted. Air
velocities should exceed 50 fpm when the window is opened to its maxi-
mum height.
DESIGN OF DUCT SYSTEMS
The duct system should be large enough to transport the fumes or
material without causing serious obstruction to the air flow. It is good
practice to proportion the ducts to obtain the desired velocities and
suction pressures at the hoods, although in many cases only an approxi-
mation to an ideal design is possible. Many exhaust hoods, and par-
*Far a discussion of spray booths, see Special Bulletin No, 16, Spray Painting in Pennsylvania, Depart-
nwa-it of Labor and Industry, 1926, HarrMmrg, Pa.
351
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
ticularly those used in buffing and polishing, are connected by short
branch pipes to the main duct which renders proportioning impractical.
Construction
The ducts leading from the hoods to the exhaust fan should be con-
structed of sheet metal not lighter than is shown in Table 4. The piping
should be free from dents, fins and projections on which refuse might
catch.
All permanent circular joints should be lap-jointed, riveted and sol-
dered, and all longitudinal joints either grooved and locked or riveted
and soldered. Circular laps should be in the direction of the flow, and
piping installed out-of-doors should not have the longitudinal laps at the
TABLE 4. GAGE OF SHEET METAL TO BE USED FOR VARIOUS DUCT DIAMETERS
DIAMETER OP DUCT
GAGE OP MSTTAL
8 in. or less „
24
9 to 18 in
22
19 to 25 in. _ .
20
26 in. or more
18
bottom. Every change in pipe size should be made with an eccentric
taper flat on the bottom, the taper to be at least 5 in. long for each inch
change in diameter. All pipes passing through roofs should be equipped
with collars so arranged as to prevent water leaking into the building.
The main trunks and branch pipes should be as short and straight as
possible, strongly supported, and with the dead ends capped to permit
inspection and cleaning. All branch pipes should join the main at an
acute angle, the junction being at the side or top and never at the bottom
of the main. Branch pipes should not join the main pipes at points where
the material from one branch would tend to enter the branch on the
opposite side of the main.
Cleanout openings having suitable covers should be placed in the main
and branch pipes so that every part of the system can be easily reached in
case the system clogs. Either a large cleanout door should be placed
in the main suction pipe near the fan inlet, or a detachable section of
pipe, held in place by lug bands, may be provided.
Elbows should be made at least two gages heavier than straight pipe
of the same diameter, the better to enable them to withstand the addi-
tional wear caused by changing the direction of flow. They should pref-
erably have a throat radius of at least one and one-half times the diameter
of the pipe.
Every pipe should be kept open and unobstructed throughout its entire
length, and no fixed screen should be placed in it, although the use of
a trap at the junction of the hood and branch pipe is permissible, provided
it is not allowed to fill up completely.
The passing of pipes through fire-walls should be avoided wherever
possible, and sweep-up connections should be so arranged that foreign
material cannot be easily introduced into them.
At the point of entrance of a branch pipe with the main duct, there
259
CHAPTER 21 — INDUSTRIAL EXHAUST SYSTEMS
should be an increase in the latter equal to their sum. Some state codes
specify that the combined area be increased by 25 per cent. While this
is not always necessary and is frequently done at the expense of a reduced
air velocity, it is none the less advisable where future expansion of the
exhaust system is contemplated.
TABLE 5. AIR SPEEDS IN DUCTS NECESSARY TO CONVEY VARIOUS MATERIALS
MATERIAL Am VELOCITIES
(FPM)
Grain dust _„! 2000
Wood chips and shavings _ _ • 3000
Sawdust i 2000
Jute dust _ _ „ ; 2000
Rubber dust. - _ I 2000
Lint. 1500
Metal dust (grindings) 2200
Lead dusts „ j 5000
Brass turnings (fine) I 4000
Fine coal
4000
Air Velocities in Ducts
When the static suction has been fixed for a given hood, the air velocity
in the duct may be determined from Equation 2. Air velocities for
conveying a material should be moderate. Table 5 gives the velocities
generally employed for conveying various substances. Equations 5a and 5b
may be used as tests to determine the conveying efficiency of a system6.
Velocities determined from these formulae should be increased by at least
25 per cent since they represent the minimum at which a stated size and
density of material can be transported.
For vertical ducts: V = 13,300 y^y d*-™ (5a)
For horizontal ducts: V = 6000 y—y <#»•*» (5b)
where
V = air velocity in duct, feet per minute.
5 — specific gravity of particles.
d = average diameter of largest particles conveyed, inches.
Example 2. Granular material, the largest size of which is approximately 0.37 in. in
diameter, with a specific gravity of 1.40 is to be conveyed in a vertical pipe the velocity
of the air in which is 4100 fpm; find whether the material can be transported at this
velocity.
Substitute data in Equation 5a and multiply by 1.25:
V = 1.25 X 13,300 X ~| X 0.37'-*7
Antilog (0.57 X log 0.37) = 0.568; the required velocity is, therefore, 5500 fpm.
Hence, the duct velocity must be increased either by speeding up the fan or decreasing
th« diameter of the duct, or both.
*DaHaValleF J. M.: Determining Minimum Air Velocities for Exhaust Systems. (A.S.H.V.E. Journal
Section, Heating, Piping and Air Conditioning, September, 1932).
353
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Duct Resistance
The resistance to flow in any galvanized duct riveted and soldered at
the joints may be obtained from Fig. 3, Chapter 20. The pressure drop
through elbows depends upon the radius of the bend. For elbows whose
centerline radii vary from 50 to 300 per cent of pipe diameter, the loss may
be estimated from Table 6. It is sometimes convenient to express the
resistance of an elbow in terms of an equivalent length of duct of the same
diameter. Thus with a throat radius equal to the pipe diameter the
resistance is equivalent to a section of straight pipe approximately 10
diameters long, while with a throat diameter radius lJ/£ times the dia-
meter, the resistance is about the same as that of seven diameters of
straight pipe.
COLLECTORS
The most common method of separating the dust and other materials
from the air is to pass the mixture through a centrifugal or cyclone
collector. In this type of collector the mixture of the air and material
is introduced on a tangent, near the cylindrical top of the collector, and
the whirling motion sets up a centrifugal action causing the compara-
tively heavy materials suspended in the air to be thrown against the side
of the separator, from which position they spiral down to the tail piece,
while the air escapes through the stack at the center of the collector.
The diameter of the cyclone should be at least 3}^ times the diameter
of the fan discharge duct. When two or more separate ducts enter a
cyclone, gates should be provided to prevent any back draft through a
system which may not be operating. Cyclones working in conjunction
with two or more fans should be designed to operate efficiently at two-
thirds capacity rating. The following formula is useful in computing the
loss through a cyclone when the velocity of the air in the fan discharge
duct is known :
where
#c = the pressure drop through the cyclone, inches of water.
V = the air velocity in the fan discharge duct, feet per minute.
If a cyclone is used to collect light dusts such as buffing wheel dusts,
feathers and lint, the exhaust vent should be large enough to permit an
air velocity of 200 to 500 fpm. This will, of course, require a cyclone of
larger dimensions than given for the foregoing general case.
When a high collection efficiency is desired, or the material is very fine,
multicyclones may be used, These are merely small cyclones arranged in
parallel which utilize the principle of high centrifugal velocity to attain
separation. The capacities and characteristics of this type of separator
should be obtained from the manufacturers.
Cfot-h Filters
Filter cloths are used when the material collected by an exhaust system
is valuable or cannot be separated from the air with an ordinary cyclone,
CHAPTER 21 — INDUSTRIAL EXHAUST SYSTEMS
They are also employed when it is desirable to recircuiate the air drawn
from a room by the exhaust system, which otherwise might entail con-
siderable loss in heat. Bag niters which are properly housed may be
operated under suction. Bag houses used in the manufacture of zinc oxide
and other chemical products are operated on the positive side of the fan.
Wool, cotton and asbestos cloths are commonly used as filtering
mediums. When woolen cloths are employed, the filtering capacities vary
from }/2 to 10 cfm per square foot of filtering surface, depending on the
character of the material collected. The rates for cotton and asbestos
cloths are slightly lower. The type of filter cloth and the rates of filtration
depend, of course, on the material to be collected and the fan capacity.
The time increase of resistance varies with the amount of material per-
mitted to build up on the surface of the filter and can be determined only
by experiment. The limits of the increase may be regulated by adjust-
ment of the shaking or cleaning mechanism. These limits may be
regulated further according to the capacity of the fan and the effective
performance of the hoods and the duct system.
RESISTANCE OF SYSTEM
The maintained resistance of the exhaust system is composed of three
factors: (1) loss through the hoods, (2) collector drop, and (3) friction
drop in the pipes.
The loss through the hoods is usually assumed to be equal to the suction
maintained at the hoods. The collector drop in inches of water is given
approximately by Equation 6, but where possible the resistance of the
particular collector to be used should be ascertained from the manu-
facturer.
Friction drop in the pipes must be computed for each section where
there is a change in area or in velocity. Find the velocities in each section
of pipe starting with the branch most remote from the fan. The friction
drop for these sections can be determined by reference to Table 6. Total
friction loss in the piping system is the friction drop in the most remote
branch plus the drop in the various sections of the main, plus the drop
in the discharge pipe.
SELECTION OF FANS AND MOTORS
Manufacturers generally provide special fans for the collection of
various industrial wastes. These are available for the collection of coal
dust, wood shavings, wool, cotton and many other substances. For
particular features concerning special fans, consult the Catalog Data
Section of THE GUIDE and manufacturers* data. When substances
having an abrasive character are conveyed^ the fan blades and housing
should be protected from wear. This may be accomplished by placing a
collector on the negative side of the fan or by lining the housing and
blades with rubber.
If no future expansion of an exhaust system is contemplated, the fart
motor should be chosen to provide the calculated air volume. Should,
however, the exhaust system be required to handle more air in the
future, the motor should be adequate for the maximum load anticipated..
355
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Further information regarding the choice of fans and motors is given in
Chapter 17.
PROTECTION AGAINST CORROSION
The removal of gases and fumes in many chemical plants requires that
metals used in the construction of the exhaust system be resistant to
TABLE 6. Loss THROUGH 90-DEG ELBOWS
ELBOW CENTRE LENH RADIUS IN PBB CENT
or PIPE DIA,MZTEB
Loss n? PEE CENT OF VELOCITY HEAD
50
100
150
200 to 300
75
26
17
14
chemical corrosion. A list of the materials which may be used to resist
the action of certain fumes is given in Table 7. Hoods and ducts when
short, may frequently be constructed of wood and be quite effective,
TABLE 7. MATERIALS TO BE USED FOR THE PROTECTION OF
EXHAUST SYSTEMS AGAINST CORROSION
TTPB OF FUME COJTVETBD
PROTECTIVE MATERIAL TO BE USED
Chlorine .
Hydrogen sulphide
Ammonia. -
Rubber lining or chrome-nickel alloys
Aluminum coated iron, aluminum, high chrome-nickel alloys
Iron or steel
Sulphurous gases
Hydrochloric acid-
Nitrous gases
High chrome-nickel alloys
Rubber lining, chrome-nickel alloys
Nickel-chrome alloys
^Condensed from data given by Chilton and Huey (Industrial and Engineering Chemistry, Vol. 24, 1932).
Rubberized paints are available and may be applied as protective coatings
in handling such gases and fumes as chlorine and hydrochloric acid.
PROBLEMS IN PRACTICE
1 • Should individual operations be served by an individualized dust collector
system?
Yes, if operations are usually kept individual in a group of machines.
2 • Axe state regulatory requirements as to suction applicable to all sorts of
dust collecting installations?
As a rule the regulations refer only to grinding wheel and buffing wheel systems. They
are needed for many other industrial processes.
CHAPTER 21 — INDUSTRIAL EXHAUST SYSTEMS
3 • What is the most common method of reducing total air yolumes handled
in cases employing large hoods over apparatus covering a large area?
The use of the petticoat or double hood which permits a comparatively high air velocity
at the rim of the hood and controllably small velocities in the center.
4 • What other types of collectors are available for use in the place of cyclones
and niters when chemical and physical conditions obviate the possibility of the
use of them?
Devices such as scrubbers and contactors, using water or other contacting liquids,
electrical precipitators, and dynamical precipitators.
5 • What is the most frequent error made in dust collector system design?
The omission of some means of putting into the workroom air having the proper charac-
teristics to replace that which has been exhausted.
6 • Are there available means for testing the performance of dust collecting
systems when they are required to meet high industrial hygienic standards?
Yes. Such means are set up by the United States Public Health Service and by the
Standard Code for Testing Centrifugal Fans (Chapter 41).
7 • Why is it not permissible to connect up emery wheels and buffing wheels to
the same exhaust system?
Emery wheels and buffing wheels should be handled by separate systems because of the
fire hazard, as it is possible for sparks from the emery wheels to ignite the lint and dust
from the buffing wheels when both are carried through the same system.
3 • Give an important characteristic of centrifugal type dust collectors which
should be given consideration when applying this type of collector to instal-
lations requiring high separating efficiencies.
The separating action of a cyclone or centrifugal type collector depends largely on
centrifugal force. Reducing the radius of air flow increases the centrifugal force for a
given velocity of flow. Accordingly, the smaller size units usually give higher separating
factors, and better results can sometimes be obtained by using a number of small col-
lectors instead of one large unit.
9 • Mention some general suggestions relating to the design of efficient in-
dustrial exhaust systems.
a. Endeavor to obtain a maximum degree of effectiveness with a minimum volume of air,
by the use of well designed hoods closing in the sources of fumes or material to be removed
so located as to take advantage of the natural direction taken by the fumes or materials
when leaving their source.
b. Give particular care to the velocity of flow. The duct velocities for material con-
veying systems must be high enough to properly carry the material, but they should not
be higher than necessary because excessive velocities increase the pressure requirements
and result in a waste of power.
c. Select the type of fan best suited to the job. For installations where stringy material
is handled do not use a fan wheel which has a shroud.
J. When handling the refuse from various machines, study the grouping and operating
cycles of the machines. Connecting a large number of machines into one system is
frequently very uneconomical.
e. Avoid unnecessary distances and bends in laying out the piping system.
10 • The static pressure measured at the throat of a buffing wheel hood is 2 in.
and the velocity head measured with a Pi tot tube is 1.6 in. Calculate the
restriction coefficient f.
357
AMERICAN SOCIETY of. HEATING and VENTILATING ENGINEERS GUIDE, 1935
From Equation 2, V = 4005 / V~ht-
From the theory of air flow, V = 4005 \/ hv.
Hence, \/Tv - /
1.1 • A tank} 4 ft by 8 ft, contains a fluid which gives off injurious vapors. A
large hood is located 30 in. above the top of tfce tank and extends slightly over
its edges. Assuming that a velocity of 60 fpm is required to adequately control
the vapors near the edges of the tank, calculate the air flow required.
Using Equation 4, P ; = 2 X 4 -f 2 X 8 = 24 ft; D = 30 inches = 2.5 ft; V = 60 fpjn.
Hence, Q = 1.4 X 24 X 2.5 X 60 - 5.040 cfm.
12 • Silica dust with a specific gravity of 2.65 is being conveyed in a duct system;
The velocity measured in a vertical portion of the system is found to be 2700
fpm. What is the maximum diameter particle transported at this velocity?
Using Equation 5a, 2700 =* 13,300 X ~~ X ^-57°
o.OO
from which
d » (0.28)1-75 - 0.11 in.
358
Chapter 22
FAN SYSTEMS OF HEATING
Types of Systems, Blow -Through, Draw-Through, Heating Units,
Design, Temperatures, Weight of Air to be Circulated, Tempera-
ture Loss in Ducts, Heat Supplied Heating Units and Washer,
Grate Area, Boiler Selection, Weight of Condensate, Static Pres-
sure, Fans and Control
A FAN system of heating depends upon fans and blowers to distribute
air through ducts from one centrally located plant. This chapter
considers heating and humidifying systems of this type whereas similar
systems arranged for cooling and dehumidifying are discussed in Chapter
9. A special type of central fan system, the mechanical warm air or fan
furnace system, which is especially adapted to residences, churches, halls,
and other small buildings, is covered in Chapter 23.
TYPES OF SYSTEMS
In the indirect type of central fan heating and air conditioning systems,
steam is usually the medium by which heat is transferred from the boiler,
or other source of heat, to the heating units. If the system is intended
solely for heating, the air is passed over one or more stacks or batteries of
heating units and then conveyed to the spaces for which it is intended
through a system of ducts. In some cases, a predetermined amount of
outside air is introduced for ventilating purposes, whereas in others the
moisture content is controlled by passing the air through a washer or
humidifier. If the apparatus is designed to control simultaneously the
temperature, humidity, air motion, and distribution, it is known as an air
conditioning system.
In the split system, the heating is accomplished by means of radiators or
convectors, and the ventilating or air conditioning by means of the central
fan apparatus. In the combined system, the entire operation of heating,
ventilating, and air conditioning is handled by the central fan system.
A common arrangement of the central fan system of heating is illus-
trated by Fig. 1 and consists of a fan, a heating unit (heater) enclosed by a
sheet metal casing connected with the suction side of the fan, a sheet1
metal casing connected to the heating unit casing run to the outside of the"
building and provided with an adjustable opening inside the building for
recirculation of the air when desired, and a duct system attached to the
fan outlet to convey and distribute tlie air to various parts of the building
to be warmed by the apparatus. The fan is ordinarily motor-driven ; there
are, Ifo^ever, many cases when a direct-connected steam engine may be
used to advantage. In this event the exhaust from the engine can be cori-
359
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
nected to one or more sections of the heater, depending upon the con-
densation rate of the engine. The recirculation duct connected with the
opening in the suction duct should be extended to a point as near the
floor as possible.
When ventilation is not a requirement or is considered relatively unim-
portant, as in shop and factory heating, and the number of persons vitiat-
ing the air is small compared with the cubical contents of the building, or
the process does not generate obnoxious gas or vapors, the air may be
recirculated, sufficient outside air for ventilation being supplied by infiltra-
Rotting Shutter-
Oubid* Wall
By-pass Damper
FIG. 1. ARRANGEMENT OF A CENTRAL FAN HEATING SYSTEM
(DRAW-THROUGH)
Canvas Connection
Heater
Foundation
V
_
Supply Duct |
By-pass Damper
Floor
FIG. 2. ARRANGEMENT FOR HEATING UNIT (BLOW-THROUGH)
tion. The amount of heat to be supplied the heating unit in this case is the
same as would be required for a direct radiation installation.
When ventilation is a requirement to be met, an arrangement similar to
that shown by Fig. 1 may be employed. Since the amount of air necessary
for heating is generally in excess of the amount required for ventilation,
considerable fuel economy may be effected by recirculating a portion of
the air. In this case only sufficient outside air is drawn into the system to
meet the ventilation requirement and the remainder of the air, required
for heating, is recirculated. This may be readily effected by an arrange-
ment of ducts and dampers on the suction side of the fan as previously
mentioned. If the outside air introduced is to be washed or conditioned
the washer or humidifier and tempering coil may be added between the
inlet for the recirculated air and the fresh air intake.
360
CHAPTER 22 — FAN SYSTEMS OF HEATING
Blow-Through, Draw-Through
When the heating unit is located on the suction side of the fan, the
system is known as draw-through. (See Fig. 1.) When the heating unit
is located in the discharge from the fan, the system is known as blow-
through. (See Fig. 2.) The draw-through combination is used for factory
and toilet room installations because a more compact arrangement of
the apparatus usually is possible. In addition, air leakage will be inward.
The blow-through combination is used principally in schools and public
buildings, and for all booster coil arrangements where different tempera-
tures and independent temperature regulation are required for different
heated spaces. In public building installations, the fan frequently blows
the heated air into a plenum chamber from which the air ducts radiate to
the various rooms of the building; this arrangement is sometimes called
the plenum system.
HEATING UNITS
The heating units for central fan systems using steam as the heating
medium may be classified as (1) tempering coils, (2) preheater coils, (3)
reheater coils, (4) booster coils, and (5) water heaters, either open or
closed. Tempering coils are used with ventilating and air conditioning
systems for raising the temperature of the outside cold air to above freez-
ing, or 32 F. They are not required for heating systems where all of the
air is recirculated, since the temperature of the recirculated air will be
above freezing. Preheater coils are used with air conditioning systems to
raise the temperature of the air from that leaving the tempering coils to
such a temperature that in passing through the water sprays of the washer
(without water heater) the air will become partially saturated (adia-
batically) having a moisture content corresponding to the required dew-
point temperature. Preheater coils therefore supply heat as necessary to
control the dew-point temperature. The reheater coils are used to raise the
temperature of the air leaving the tempering coils (in the case of a heating
or ventilating system) or the air leaving the washer (in the case of an air
conditioning system) to that necessary to maintain the desired tempera-
ture in the rooms or spaces to be heated or conditioned, except where
booster coils are used, in which case the reheater coils raise the air tem-
perature to approximately room temperature, or slightly higher. Booster
coils are installed in the duct branches to control the temperature of the
air entering the rooms or spaces for which it is intended. Water heaters are
used on an air conditioning system to control the dew-point temperature.
They are used mainly for industrial work, seldom for comfort conditioning.
They are not used where preheater coils are employed. The open type
supplies steam directly to the spray water, while the closed type utilizes a
heat interchanger by which the steam imparts its heat to the spray water.
Where water heaters are required for comfort conditioning, the closed
type is used.
The heating units for central fan systems in use at the present time con-
sist either of pipe coils, finned tubes of steel, copper, brass or other metal,
cast-iron sections with extended surfaces, or the cellular type. Steam is
passed through these heating units and the air to be heated is passed over
their exterior surfaces.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
In selecting a heating unit for any particular service, the choice should
be based on the desired requirements as follows:
1. Final temperature desired.
2. Loss in pressure for friction) of air passing over the heating unit.
3. Air velocity over the heating unit.
4. Free area or face area of heating unit.
5. Ratio of heating surface to net free (or face) area.
6. Air volume required.
7. Number of rows of pipes, tubes, or sections.
8. Amount of heating surface.
9. Steam pressure drop through the heating unit.
10. Weight of heating unit.
Final Temperature Desired. The choice of a heating unit is Jargely
influenced by the final temperature desired, when the entering air tem-
perature and steam pressure available at the heating unit are specified.
These data are obtainable from manufacturers' catalogs.
Loss in Air Pressure (or Friction). The allowable friction through the
heating unit is one of the first factors to be determined in the selection of
the apparatus. The velocities of air through various types of heating
units will not necessarily be the same, but for any particular job the
velocity through the heating unit should be a secondary consideration and
the allowable friction or air pressure loss should be fixed approximately
before proceeding with the selection of the heating unit. The loss in air
pressure (or friction) through the heating unit should not exceed a pre-
determined maximum allowable amount for economical operation and for
moderate size and first cost of installation.
In public building work, the maximum allowable friction through both
tempering coil and reheater coils should never exceed ^ in. of water and
it is advisable that the friction be kept considerably lower than this figure
if possible. A tempering coil friction ranging from 0.10 to 0.20 in. of water
is considered satisfactory. The air pressure loss for reheaters ordinarily
ranges from 0.20 to 0.40 in. of water. In factory work, the maximum
friction through the heater should never exceed 0.8 in. or 1 in. of water
and it is advisable to figure the heaters at lower frictions if possible.
Velocity through Heating Unit. This velocity has generally been given
in manufacturers* tables as being measured at 70 F and in most cases
refers to the velocity through the net free area of the heating unit, or
through the net space between the pipes, tubes or sections. Although
most manufacturers give suitable velocities measured at 70 F, certain
manufacturers show velocities measured at 65 F and others indicate
velocities measured at the average air temperature through the heating
unit. Many new heating units, however, specify net face areas with cor-
responding velocities instead of velocities through net free areas. In
either case, manufacturers publish the corresponding friction or air-
pressure loss in tables. The velocity through the net free area of the
heating unit averages about 1000 fpm and that through the net face area
about 500 fpm.
The volume of air to be heated in any particular case is determined after
consideration of the ventilation requirements, heat losses, and quantity of
air required for proper circulation, as explained in Chapters 2 and 7.
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CHAPTER 22 — FAN SYSTEMS OF HEATING
The number of rows of pipes, tubes, or sections or the amount of heating
surface to be used may be selected from manufacturers' catalogs after the
quantity of air handled and the heat load are known. Savings in oper-
ating expense or cost of installation should result from a proper selection
of heater and by-pass areas. For example, instead of having the entire
air quantity go through a one-row heating unit, it may be advantageous
to use a two-row heating unit and a properly sized by-pass. Thus, when
no heating is being done, a suitable by-pass damper may be opened to
place a lighter load on the fan.
The steam pressure drop through the heating unit is also tabulated in
manufacturers* data tables. The sizing of steam supply and return
piping, allowing for drops through heating units, is explained in Chapter
32.
Weight of Heating Unit. In the design of a heating system, the weight
limitations of heating units are determined by the location of the units.
Obviously, if there is no loading limitation imposed, any type of heating
unit may be selected. On the other hand if the heating unit is to be hung
from the ceiling, it may be desirable to use the lightest unit which will
accomplish the work required.
DESIGNING THE SYSTEM
The general procedure for the design of central fan systems is as
follows :
1. Calculate the heat loss for each room or space to be heated.
2. Determine volume of outside air to be introduced,
3. Assume or calculate temperature of air leaving registers or supply outlets.
4. Calculate weight of air to be circulated.
5. Estimate temperature loss in duct system.
6. Calculate heat to be supplied the heating units and washer.
7. Select heating units and washer from manufacturers* data and performance curves.
8. Calculate total heat to be supplied,
9. Calculate grate area and select boiler.
10. Design duct system.
11. Calculate total static pressure of system.
12. Select fan, motor, and drive.
The heat losses (If) should be calculated in accordance with the pro-
cedure outlined in Chapter 7. If a positive pressure is maintained by the
central fan system in the room or space to be ventilated or conditioned,
there will ordinarily be very little infiltration of cold outside air through
the cracks and crevices of the space. Consequently, the volume of air
introduced into the space at the assumed or calculated outlet temperature
need only be sufficient to provide for the transmission losses, plus about
one-third of the infiltration losses. The exfiltration of heated or con-
ditioned air through the cracks and crevices of the space should be pro-
vided for by making the usual allowance for the infiltration losses in
arriving at the total heat loss of the space. The air required to make up
for this exfiltration of heated or conditioned air will be brought in at the
outside air intake and may be included as a part of the outside air neces-
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
sary for the ventilating requirements. The heat required to raise this air
to the conditions maintained in the room must be provided by the tem-
pering coils, preheater coils, and reheater coils. If a positive pressure is
not maintained in the room or space to be conditioned, the normal in-
filtration of outside cold air will take place in this room, and the outlet
temperature, together with the required air volume at this temperature,
must be sufficient to provide for both infiltration and transmission losses.
Volume of Outside Air
The volume of outside air required for ventilation or air conditioning
purposes may be determined from data in Chapter 2. In no case shall
less than 10 cfm per person be introduced.
The heat required to warm the outside air introduced for ventilation
purposes (Ho) may be determined by means of the following formula:
Ho « 0.24 (t - to) M0 (1)
where
0.24 = specific heat of air at constant pressure.
/ = room temperature, degrees Fahrenheit.
to = outside temperature, degrees Fahrenheit.
MO — weight of outside air to be introduced per hour, in pounds = d0Q0.
Qo = volume of outside air to be introduced, cubic feet per hour.
d0 — density of air at t0, pounds per cubic foot.
Example 1 . A building in which the temperature to be maintained at 70 F requires
10,000 cfm. If the outside temperature is 20 F, how much heat will be required to warm
the air introduced for ventilation purposes to the room temperature?
Solution. Qo = 10,000 X 60 = 600,000 cfh; d0 » 0.08276 (Table 3, Chapter 1);
Mo = 0.08276 X 600,000 = 49,656 Ib; t = 70 F; t0 = 20 F; H0 « 0.24 X (70 - 20)
X 49,656 = 595,872 Btu per hour.
Temperature of Air Leaving Registers
If the system is to function only as a heating system, that is, entirely as
a recirculating one, the temperature of the air leaving the register outlets
must be assumed. For public buildings, these temperatures may range
from 100 to 120 F, whereas for factories and industrial buildings the out-
let or register temperature may be as high as 140 F. In no case should the
outlet temperature exceed these values.
For ventilating or conditioning systems, the temperature of the air
leaving the supply outlets may be estimated by means of the following
formula :
M (2)
where
ty = outlet temperature, degrees Fahrenheit.
H = heat loss of room or space to be conditioned, Btu per hour.
Q = total volume of air to be introduced at the temperature /, cubic feet per hour.
If the outlet temperature (ty) as determined from Equation 2 exceeds
120 F for public buildings, or 140 F for factories or industrial buildings,
CHAPTER 22 — FAN SYSTEMS OF HEATING
these respective outlet temperatures should be used as factors in the
following equation to determine the volume of air to be introduced into
the room or space:
_ 55.2H
Q ~ (h - t) (3)
Example £. The heat loss of a certain auditorium to be conditioned is 100,000 Btu per
hour. The ventilating requirements are 90,000 cu ft per hour and the room temperature
70 F. Determine the outlet temperature.
Solution. Substituting in Formula 2,
55.2 X 100,000
h 90,000
-f 70 » 131.3 F
Inasmuch as this temperature is excessive, it will be necessary to assume an outlet
temperature, which will be taken as 120 F, and to calculate the amount of air to be
introduced into the room at this temperature to provide for the heat loss. Substituting
in Equation 3,
Q _ 65^100^000 = U(WOO cfh (at temperature 0
Weight of Air to be Circulated
The total weight of air to be introduced into the room or space to be
heated or conditioned (M) is given by the following formulae:
M = Mo -f Mr (5)
Mo = doQo (6)
where
d = density of air at temperature t, pounds per cubic foot.
do = density of air at temperature /o, pounds per cubic foot.
Qo = volume of outside air at temperature to.
M0 = weight of outside air, pounds.
Mr = weight of recirculated air, pounds.
Example 8. Using the data of Example 2 and an outside temperature of 20 Ft what
will be the values of M, M0 and Afr?
Solution, d - 0.07495 ;&> =jQ,QS276;() = 110,400; Q0 - 90,000; H = 100,000.
_ 100,000
~ 0.24 X (120 - 70)
MG = 0.08276 X 90,000 - 7,448 lb
MT - M - Mo - 8,333 - 7,448 = 885 lb
Temperature Loss in Ducts
The allowances to be made for loss in transit through the duct system
(/,) are as follows:
1. When the duct system is located in the enclosure to which the air is being delivered,
as in a factory, it may be assumed that there is no loss between the r^heater cotl and the
point or points of discharge into the enclosure.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
2. For ducts in outside walls or attics, or other exposed places, allow Q.25 F per
linear foot of uninsulated duct.
3. For ducts run underground an allowance shall be made based on the estimated heat
loss of the duct, assuming the average temperature of the ground to be 55 F.
Heat Supplied Heating Units and Washer
The following cases may arise in practice :
A. The heating of the building is done entirely by means of a central fan system, all
of the air being drawn from the outside.
B. Similar to A, except that all of the air is recirculated.
C. A portion of the air is recirculated, and the remainder is drawn in from the outside.
D. Air at the same temperature is to be delivered to all the rooms. A constant relative
humidity is maintained in the building and all of the air circulated is drawn from outside
the building. (Not applicable to the heating of various rooms where individual control
of each room is desired.)
E. Outside air,- return air, and by-pass air are used with the reheater located in by-
pass air chamber.
F. Arrangement of apparatus where individual control of the temperature for .each
room is required in conjunction with air washer equipment to maintain a constant
relative humidity in the rooms. The airi "washer is provided with a water heater for the
spray water ,:capable of fully saturating the air. A section of preheater may be used for.
this purpose in place of the water heater. With this arrangement and with a uniform
temperature of air entering the rooms, it is impossible to maintain the same room tem-
perature throughout the building because the weight of air to be delivered to each room
is determined and fixed by the ventilating requirements.
In analyzing these cases, the following symbols will be used :
H = heat loss of the room or building, Btu per hour.
Hi « heat to be supplied to the reheater coil, Btu per hour.
Hz = heat supplied tempering coil, or compering >eoii and preheater* Btu per hour.
HZ = heat supplied air washer by wa#er heater, Btii per hour.
#4 = heat to be supplied booster coil, Btu per hour.
M — weight of air to be introduced into the room or building, pounds per hour.
'Mi « weight of recirculated air, pounds per hour, ,
Mb — , weight of air by-passing washer, pounds. per hour.
jlf0 ="" weight of air drawn in from outside, pounds per hour.
to — mean temperature of outside air, degrees Fahrenheit*
/ = mean air temperature to be maintained in the room or building, degrees
Fahrenheit. . .
h = mean temperature of the air entering the reheater coil.
/2 = mean temperature of the air leaving the reheater coil.
tz = temperature loss in the duct system.
ty = temperature of the air leaving the duct outlets,,;
tK — average temperature of air entering tempering coil.
&# — temperature of air entering washer.
0.24 = specific heat of air at constant pressure1.
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CHAPTER 22 — FAN SYSTEMS OF HEATING
Rolling Shutter-
/ Steam
Control Valve || _ Control Valve
-Air Leaving Fan at ty
Outside Air J
Louvres "*-*-r ,
Outside Wall
By-pass Damper
FIG. 3. HEATING UNIT AND FAN ARRANGED FOR OUTSIDE AIR CIRCULATION (Case A)
Case A . (Fig. 3) All of the air circulated to be drawn from outside the building, in
which case tx — t0.
- *o) M0 • (7)
. . ,(8)
Hi = 0.24 fe - id Mo
Example 4- The heat loss H for a certain factory building is 700,000 Btu per hour.
The mean inside temperature t to be maintained is 65 F. The assumed outside air tem-
perature to is 0 F; tz = 0, ty « /2 and is assumed to be 140 F. The temperature
leaving the tempering coil is assumed to be 35 F. Required, Hi and Hi. From Equation 4,
M *
700,000
0.24 (140 - 65)
38,889 Ib per hour.
Hi = 0.24 X (35 -Q) X 38,889 » 326,667 Btu per hour.
Hi « 0.24 X (140 - 35) X 38,889 = 980,003 Btu per hour.
•TrJs:H~ Hi .* 326,667 -1- 980,003 » 1,306,670 Btu per hour.
'Air Returned
from Heated Space
^T
CH
,Stearn
^-Automatic Valve ,
-Air Leaving Fan at ty
^Pulley
TT - ' .
/Foundation
Heater-^
\r
X
<2
Fan
I
ELEVATION
FIG. 4, ARRANGEMENT FOR RECIRCULATION (Case B)
: • (Fig. 4) All of the air is to be recirculated, in which case t\ = /.
,',, - M* = 38,889 Ib
Mi ^ 0,24 (^ - h) Mr
:..',„. Hi « 0.24 (140 - 65) X 38,889 = 700,000 Btu per hour.
This Example illustrates the saving in fuel consumption by the *^-^*-
culation of the air. The heat to be supplied the apparatus is the same ais
that required for a direct system of heating and is equal to the heat loss
of th^Fbuilding '(Hi =!H), in the example 700,000 Btu per hour as
compared with 1,306,670 for Case A.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Rolling Shutter- £
/ /S
; t Control Valve II
/ Recirculated Air || 1
' . yy/ . U J
earn
Cor
g^
' i
trol Valve
X
xAir Leaving Fan at ty
PL- Pulley
Foundation
/ Floor Line
P
^
Air Filter
~?
I
^
'2
X
Outside Air V
Louvres * *~'\
Fan
Outside Wall-J^j
By-pass Damper
FIG. 5. COMBINATION OF RECIRCULATED AIR AND OUTSIDE AIR (Case C)
Case C. (Fig. 5) A portion of the air circulated is recirculated air and the remainder,
as may be required for ventilating purposes, is drawn in from the outside. According to
Equations 4 and 5,
The temperature of the resulting mixture of outside and recirculated air entering the
tempering coil is:
~»f A I If *
(9)
M
Example 5. Assuming that a positive supply of outside air (do = 0.0864) is required
for ventilation at the rate of 90,000 cu ft per hour in the preceding example, then M0
- 0.0864 X 90,000 » 7776 Ib per hour are required, measured at 65 F.
Mr - M - M0 - 38,889 - 7776 = 31,113 Ib
Hi
7776 X 0 + 31,113 X 65 K0 ^
k~ - 38^89 - ~52F
38,889 X 0.24 (140 - 52) - 821,336 Btu.
This amount of work may be accomplished with one or more banks of heating units,
that is, either a single reheater or a tempering coil and reheater.
The three preceding cases refer to installations in which conditioning
the air to maintain certain relative humidity requirements does not enter
into the problem, as for example, certain types of industrial installations.
In practically all modern public buildings, theaters, schools, and in many
industrial installations, the ventilating requirements include the provision
for washing and humidifying the air delivered to the various rooms of the
structure.
In the following cases it is assumed that in addition to maintaining a
mean room temperature t, the heating and ventilating apparatus is
required to maintain a constant relative humidity in the rooms.
368
CHAPTER 22 — FAN SYSTEMS OF HEATING
,/ Control Valve
Steam
Rolling Shutter-
Outside Air
Louvres"^"
Outside Air t
1L
•' * Steam Control Valve
Tempering Coil
- ...
as:
\ x
jte $^
1
*w
pashe||
"^Rehe
sr
->-
^
ater
f *T^
1 ^"^sprayWat,
Fan
4
PURVIEW
FIG. 6. OUTSIDE AIR CIRCULATED; CONSTANT RELATIVE HUMIDITY IN ROOM (Case D)
Case D. (Fig. 6) The maximum relative humidity that may be maintained within the
building without the precipitation of moisture on single glazed sash when the outside
temperature is 30 F is approximately 35 per cent. If the inside temperature t is 70 F, 35
per cent relative humidity corresponds to a dew-point temperature of 41 F. (See
psychrometric chart.)
The installation shown in Fig. 6 contemplates the use of a tempering coil, an air
washer provided with a water heater, and a reh eater. The tempering coil, one section in
depth, warms the incoming air to approximately 35 F to prevent freezing any of the spray
water. The air passing through the spray chamber is saturated and leaves at a tempera-
ture of /i = 41 F.
The heat to be supplied the reheater is:
#1 = 0.24 (4 — 41) M Btu per hour.
The heat to be supplied the tempering coil is:
Hi = 0.24 (35 - t0)M Btu per hour.
The amount of heat, per pound of air circulated, to be supplied the humidifying washer
or humidifier is the difference between the heat content of the assumed dry air entering
the washer at a temperature of fw = 35 F and the leaving saturated air at t\ = 41 F
(Chapter 1), or:
15.7 — 8.4 = 7.3 Btu per pound of dry air.
The amount of heat required for the washer is:
Ha = 7.3 M Btu per hour.
The total amount of heat required by the apparatus is, therefore:
Hi -f- H3 + H3 Btu per hour.
If a washer having a humidifying efficiency of 67 per cent without water heater is em-
ployed it will be necessary to heat the outside air drawn into the apparatus by means of
the tempering and preheater coils to such a temperature that the air in passing through
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
the water sprays will become partially saturated (adiabatically) having a moisture con-
tent per pound of air equal to saturated air at 41 F. If the incoming air is warmed to
£w = 88 F (requiring a two-section-depth heating unit) it will be cooled in the washer to
64 F, with a temperature drop of 88 - 64 = 24 deg.
If the humidifying efficiency of the washer were 100 per cent, the air would become
adiabatically saturated at 52 F after a temperature drop of 88 — 52 = 36 F. The
efficiency of the washer is, however, only 67 per cent, so that the actual temperature drop
will be 0.67 X 36 deg or 24 deg, as used.
The heat to be supplied the reheater is in this case Hi = 0.24 (k - 64) M Btu per
hour, and the heat to be supplied to the tempering coil and preheater is H* = 0.24
(88 — t0) M. The total heat required by the apparatus is Hi + H*, no heat being
supplied to the washer.
FIG. 7. OUTSIDE AIR CIRCULATED; CONSTANT TEMPERATURE AND RELATIVE
HUMIDITY MAINTAINED IN EACH ROOM (Case E)
Case E. (Fig. 7) The temperature ty will ordinarily be different for each room
With
se K. (Fig. 7J ine temperature ry win
H and M fixed, 0.24 (ty - t}M = H, or
H
0.24 M
In order to provide the proper temperature for each room, a booster coil
is generally installed in each supply duct near the outlet to control the out-
let temperature.^. The amount of steam supplied to these booster units
is usually controlled automatically by individual thermostats. The heat
required by the booster coils depends on the temperature range through
which the air is heated and the quantity of air, or
0.24
- fe - tz}M
(10)
Total Heat to be Supplied
The total heat to be supplied (JET) is equal to the sum of the heat
requirements of the various heating units and the water heater of the
washer, if any, plus the allowance for piping tax. (See preceding Cases
A to E.)
CHAPTER 22 — FAN SYSTEMS OF HEATING
Grate Area, Boiler Selection
The required grate area may be determined by the following formula:
FXEXC
where
G = required grate area, square feet.
F — calorific value of fuel, Btu per pound.
C — combustion rate, pounds per square foot of grate per hour.
E = boiler and grate efficiency, per cent.
Example 6. Using the data in Example 4, and assuming coal having a calorific value
of 12,000 Btu per pound, a combustion rate of 7 Ib per square foot, and a performance
efficiency of 0.60, and neglecting the piping tax.
r__ ^1,306,670 . -
~ 12,000 X 0.60 X 7 ~ — H-
Weight of Condensate
The normal weight of condensate to be handled from central fan sys-
tems may be estimated by means of the following formula :
'where
_ 60 X Q X A*
W 55.2 X hfg
W = weight of condensate, pounds per hour.
Q — total volume of air, cubic feet per minute.
AJ = temperature rise of air, degrees Fahrenheit.
Afg — latent heat of steam in the system, Btu per pound.
Ducts and Outlets, Air Filters, Air Washers
The design of the duct system should be based on data contained in
Chapter 20. Air washers and humidifiers are described in Chapter 11.
For information on air filters, see Chapter 16.
Static Pressure
The total static pressure against which the system must operate may
be found by summing up the static losses through the complete system
from the outside air intake to the discharge outlets or nozzles. This
means that the loss due to friction must be determined for each piece of
apparatus involved. Most of these values may be obtained from manu-
facturers' data tables. For a simple system, the following static pressure
drops may be assumed :
1. Outside air inlet, comprised of screen, louver and short duct, may have a loss of
0.2 in. of water.
2. A typical oil filter at rated capacity and velocity has a drop of 0.25 in. of water.
3. The loss of one row of a standard make tempering stack equals 0.09 in. water.
4. The loss of one row of a standard make preheater equals 0.10 in. water.
5. A standard humidifier at rated velocity may have a loss of about 0,35 in. water.
6. The loss through one row of a standard make reheater equals 0.12 in. water.
7. A fair assumption for duct losses on a simple system is 0.25 in. water.
8. The static pressure for a nozzle type outlet may be taken as 0.1 in. water.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
The sum of these values equals 0.2 + 0.25 + 0.09 + 0.10 + 0.35
+ 0.12 + 0.25 + 0.1 = 1.46 in. which is the static pressure against which
the system must operate.
Fans and Control
The selection of fans and motors may be based on data contained in
Chapter 17. Because centrifugal fans reach their maximum efficiency
when working against the resistance offered by the average central fan
heating system, they are well adapted to such systems and are generally
used. Information on temperature control for central fan systems is
given in Chapter 14.
PROBLEMS IN PRACTICE
1 • What are the functions of (a) tempering coils, (b) preheating coils, (c)
reheating coils, (d) hooster coils, (e) water heaters?
a. Tempering coils raise the temperature of incoming air above the freezing point of
water.
b. Preheating coils add to the air sufficient sensible heat above the dew point of the
conditioned space to evaporate the amount of spray water required for humidification .
They are used with humidifying type air washers.
c. Reheating coils raise the air temperature from the dew point to approximately the
proper delivery temperature.
d. Booster units are used for more refined individual room temperature control.
e. Water heaters may be used in place of preheaters. The latent heat of evaporation
is then supplied directly to the water,
2 • What saving results from recirculating some of the room air and reducing
the amount of outside air?
Because outside air must be heated to room temperature, reducing the amount of outside
air produces a proportionate saving in heat or fuel.
3 • What items make up the total heating load in a central fan heating system?
1. The net heat loss from the conditioned space.
2. The heat required for evaporation of water for humidification.
3. The heat required to raise the temperature of outside air to room temperature,
4. Heat losses from pipes and ducts.
4 • Why is it necessary to determine the total static pressure of a central fan
heating system?
To select a fan of maximum efficiency and to determine the power required to operate
the fan.
5 • A group of three drafting rooms, having a total volume of 27,000 cu ft, a
transmission loss of 110,100 Btuper hour, and an infiltration loss of 34,200 Btu per
hour on the basis of 0 F outdoors and 70 F room temperature, is to be heated by
a recirculating hot blast heating system with air entering the rooms at 116 F.
How many cubic feet per minute, measured at 70 F, will be required?
Substitute in Equation 3. H = 110,100 + 34,200 = 144,300 Btu per hour; ty = 116 F;
, = 70 F; Q = = 55l°° - 173,160 cu ft per hour.
eta = 2886.
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CHAPTER 22 — FAN SYSTEMS OF HEATING
6 • In the preceding question, if the hot air loses 4 F between heater and
rooms, how many pounds of steam per hour at 1-lh gage will the heating
sections condense?
Substitute in Equation 12. Q = 2886 cfm, from solution of Question 5; At = 116 -f 4
- 70 = 50 F; hfg = 968 Btu, from steam table in Chapter 1.
... 60 X Q X At 60 X 2886 X 50 1tt0 .. ,
W " 55.2 X frg - 55.2 X 968 = 162 lb per hour'
7 • The same rooms are converted to chemical laboratories, requiring the intro-
duction of 12 changes of outside air, measured at 70 F, per hour to permit the
exhaust fans connected to the chemical hoods to maintain only a slight nega-
tive pressure in the rooms. At what temperature must the air enter the rooms
to maintain 70 F with 0 F outside?
Substitute in Equation 2. H = 110,100 + 34,200 = 144,300 Btu per hour; Q = 12 X
27,000 - 324,000 Btu per hour; * = 70 F; ty - ^? + 1 = 55'2Q^^3°° + 70
(j/ O^4r,UUU
= 94.6 F.
8 • In the preceding question, if the air drops 2 F between the heater and the
rooms, how many pounds of steam per hour at 1-lb gage will the heating
system condense?
Substitute in Equation 12. Q = 5400 cfm; At = 94.6 -f 2 = 96.6 F, from solution of
Question 7; hfs — 968 Btu, from steam table in Chapter 1.
w 60 X Q X At 60 X 5400 X 96.6 , ,
W = 55.2 X feg = 55.2 X 968 " 585 lb per hour.
9 • The combination hot blast heating and ventilating system for the dining
rooms of a hotel is to heat the rooms to 70 F with 0 F outside, and permit
the exhaust fan from the adjoining kitchen to draw 5000 cfm from the dining
rooms. The transmission losses from the dining rooms total 240,000 Btu per
hour. The infiltration into the dining rooms amounts to 1000 cfm from out-
doors and 1000 cfm from heater rooms. How many cubic feet per minute,
measured at 70 F, must be supplied the dining rooms if the air enters at 112 F?
First find the infiltration loss by substituting in Equation 1.
t = 70 F; to = 0; M0 = d X Q = 0.07495 X 60 X 1000 = 4497 lb per hour. In this case
d and Q are figured at 70 F. H0 == 0.24 (t - /0) ; M0 = 0.24 (70 - 0) X 4497 = 75,550
Btu per hour.
Next by substituting in Equation 3, find the cubic feet per hour to be circulated. H =
sum of transmission and infiltration losses in room = 240,000 -f 75,550 = 315,550 Btu
per hour; fc - 112 F;* - 70F;£ - - = 55f - 414,700 cu ft per hour.
ty — t LL£ — /u
cfm _ «g9?. = 6912
10 • In Question 9, 3000 cfm of outside air will be drawn in by the supply fan
and 3912 cfm will be recirculated. What will be the output of the heating
sections in Btu per hour if there is a loss of 2 F between the heaters and the
room?
The average temperature of the mixture of outdoor and recirculated air entering the
heater - 30Q° X ^ ^^ X 7° = 39.6 F. Air leaves the heater at 112 + 2 = 114 F.
691.2
Referring to Equation 12, W X kfg = total heat required per hour = - =g-= - - = H.
55.2
I cfm; At = H4 - 39.6 - 74.4 F. H - 60X6912^74.4
per hour.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
11 • When the outdoor wet- and dry-bulb temperatures are 0 F, a certain print-
ing shop is to be maintained at 75 F and 40 per cent relative humidity by means
of an air conditioning system having tempering sections, an air washer, and
reheating sections. The transmission loss is 80,000 Btu per hour and the
infiltration is 10,000 cu ft per hour, measured at 0 F. No outside air connection
is provided. How many pounds of air per hour at 120 F must be discharged
to the shop?
Infiltration heat loss, by Equation 1 = H0 = 0.24 (t - t0] MQ. By Equation 6, M0 =
d0Q0 = 0.08636 (from Table 5, Chapter 1) X 10,000 = 863.6 Ib per hour; t = 75 F;
to = 0 F; Ho = 0.24 (75 - 0) 863.6 = 15,544 Btu per hour. Total heat loss in room
= 80,000 4- 15,544 = 95,544 Btu per hour = H.
To secure the total weight of air to be introduced into the space, substitute in Equation
A *, H 95,544 00_ ., ,
4' M = 0.24 (fr -1) ~ 0.24(120-75) = 8846 lb pef h°Ur'
12 • In the preceding example: (a) How many Btu per hour are used to heat
the room? (b) How many pounds of water must be evaporated per hour to
humidify the space? (c) How many Btu will be required to evaporate this
water, basing the latent heat of evaporation on the approximate figure of
1050 Btu?
a. Btu to heat room == 95,544 as derived in preceding solution.
b. Saturated air at 75 F contains 0.01877 lb of water vapor per pound of dry air. At
40 per cent relative humidity the air would contain 0.40 X 0.01877 = 0.00750 lb of
water vapor per pound of dry air; at 0 F, saturated air contains 0.00078 lb of water
vapor per lb of dry air. The amount of water vapor required to humidify the air =
0.00750 - 0.00078 = 0.00672 lb per cu ft. Infiltration amounts to 863.6 lb per hour as
derived in the preceding solution, so 863.6 X 0.00672 = 5.80 lb of water vapor per hour
required.
c. The heat required to evaporate this water = 5.80 X 1050 = 6090 Btu per hour.
374
Chapter 23
MECHANICAL WARM AIR FURNACE
SYSTEMS
Fan Furnaces, Fans and Motors, Elimination of Noise, Air Washers
and Filters, Cooling^ Methods, Duct Design, Controls, Selecting
the Furnace, Selecting the Fan, Humidity Provision for Cooling *
System, Heavy Duty Fan Furnaces
MECHANICAL warm air or fan furnace heating systems, which are a
special type of central fan systems, are particularly adapted to
residences, small office buildings, stores, banks, schools, and churches.
Circulation of air is effected by motor-driven fans instead of by the
difference in weight between the heated air leaving the top of the casing
and the cooled air entering its bottom, as in gravity systems described in
Chapter 24. The advantages of mechanical systems, as compared with
gravity systems are:
1. The furnace can be installed in a corner of the basement, leaving more basement
room available for other purposes.
2. Basement distribution piping can be made smaller and can be so installed as to
give full head room in all parts of the average basement, or be completely concealed
from view except in the furnace room.
3. Circulation of air is positive, and in a properly designed system can be balanced in
such a way as to give a greater uniformity of temperature distribution.
4. Humidity control is more readily attained.
5. The air may be cleaned by air washers or filters, or both.
6. Some cooling effect in summer will result from the installation of a properly
designed system-
7. The fan and duct equipment may be utilized for a complete cooling and dehumidi-
fying system for summer, using either ice, mechanical refrigeration, or low temperature
water for cooling and dehumidifying, or adsorbers for dehumidifying.
8. The use of the fan increases the volume of air which can be handled, thereby
increasing the rate of heat extraction from a given amount of heating surface and
insuring sufficient air volume to obtain proper distribution in a large room.
Much of the equipment used in central fan systems is the subject matter
of other chapters. It is the purpose of this chapter to discuss the co-
ordinated design and to deal in detail only with problems not covered
elsewhere which refer particularly to the whole problem of fan warm air
furnace heating and air conditioning.
FAN FURNACES
Furnaces for mechanical warm air systems may be made of cast-iron,
steel, or alloy. Cast-iron furnaces are usually made in sections and must
be assembled and cemented or bolted together on the job. Steel furnaces
are made with welded or riveted seams. The proper design of the furnace
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
depends largely on the kind of fuel to be burned. Accordingly, various
manufacturers are making special units for coal, oil and gas. Each type
of fuel requires a distinct type of furnace for highest efficiency and econ-
omy, substantially as follows:
1. Coal Burning:
a. Bituminous — Large combustion space with easily accessible secondary radiator
or flue travel.
b. Anthracite or coke — Large fire box capacity and liberal secondary heating
surfaces.
2. Oil Burning:
a. Liberal combustion space.
b. Long fire travel and extensive heating surface.
3. Gas Burning:
a. Extensive heating surface.
b. Close contact between flame and heating surface.
A combustion rate of from 5 to 8 Ib of coal per square foot of grate per
hour is recommended for residential heaters. A higher combustion rate is
FIG. 1. USUAL METHOD OF BAFFLING ROUND CASINGS FOR FAN FURNACE WORK
A. Liner, 1 in. from casing. B. Hole to vent baffle.
C. Baffle, closed top and bottom. D. Outer casing.
permissible with larger furnaces for buildings other than residences,
depending upon the ratio of grate surface to heating surface, firing period,
and available draft.
Where oil fuel is used, care must be exercised in selecting the proper size
and type of burner for the particular size and type of furnace used. It is
recommended that the system be designed for blow-through installations,
so that the furnace shall be under external pressure in order to minimize
the possibility of leakage of the products of combustion into tlie air
circulating system.
In residential furnaces for coal burning, the ratio of heating surface to
grate area will average about 20 to 1 ; in commercial sizes it may run as
high as 50 to 1, depending on fuel and draft. Furnaces may be installed
singly, each furnace with its own fan, or in batteries of any number of
furnaces, using one or more fans.
Casings are usually constructed of galvanized iron, 26-gage or heavier,
but they may also be constructed of brick. Galvanized iron casings should
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CHAPTER 23 — MECHANICAL WARM AIR FURNACE SYSTEMS
be lined with black iron liners, extending from the grate level to the top of
the furnace and spaced from 1 in. to 1 J^ in. from the outer casing. Casings
for commercial or heavy duty furnaces, if built of galvanized iron, should
be insulated with fireproof insulating material at least 2-in. thick. It is
generally believed that either brick or sheet metal casing should be
equipped with baffles to secure impingement of the air to be heated
against the heating surfaces. Brick furnace casings should be supplied
with access doors for inspection.
For furnace casings sized for gravity flow of air, where a fan is to be
used, many manufacturers recommend the use of special baffles to restrict
the free area within the casing and to force impingement of the air against
the heating surfaces. The method of making these baffles for furnaces
with ^ top horse-shoe radiators and for furnaces with back crescent radia-
tors is illustrated in Fig. 1.
Either square or round casings may be used. Where square casings are
used, the corners must be baffled to reduce the net free area and to force
impingement of air against the heating surfaces. Fig. 2 shows the usual
method of baffling square furnace casings for fan-furnace work.
FIG. 2. METHOD OF BAFFLING SQUARE FURNACE CASING FOR FAN FURNACE WORK
A . Baffle, closed top and bottom,
casing. C. Outer casing. D.
B. Liner, 1 in. from
Hole to vent baffle.
The hood or bonnet of the casing above the furnace should be as high
as basement conditions will allow, to form a plenum chamber over the top
of the furnace. This tends to equalize the pressure and temperature of the
air leaving the bonnet through the various openings. It is generally con-
sidered advisable to take off the warm air pipes from the side of the bonnet
near the top, as this method of take-off allows the use of a higher bonnet
and thus provides a larger plenum chamber. Fig. 3 illustrates a complete
residence fan furnace installation showing location of fan, furnace, filters,
plenum chamber and method of take-off of warm air pipe.
FANS AND MOTORS
Centrifugal type fans are most commonly used, and these may be
equipped with either backward or forward curved blades. Low tip speed
is desirable for the elimination of air noise, especially where forward
curved blades are used. Motors may be mounted on the fan shaft or
outside of the fan with belt connection. Multi-speed motors or pulleys
377
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
are desirable to provide a factor of safety and to allow for more rapid
circulation for summer cooling.
For additional information on fans and motors, see Chapter 17.
NOISE ELIMINATION
Special attention must be given to the problem of noise elimination.
The fan housing must not be directly connected with metal, either to the
furnace casing or to the return air piping. It is common practice to use
canvas strips in making these connections. Motors and their mountings
FIG. 3. COMPLETE RESIDENCE FAN FURNACE INSTALLATION SHOWING LOCATION OF FAN,
FURNACE, FILTERS, PLENUM CHAMBER AND METHOD OF TAKE-OFF OF WARM AIR PIPE
A. Transition fitting.
B. Filters.
C. Capped opening.
D. Canvas connection.
E. Pulley — 3 diam. V-type.
F. Eliminator.
G. Solenoid valve.
H. Pressure gage.
J. Water supply.
K. Drain.
must be carefully chosen for quiet operation. Electrical conduit and
water piping must not be fastened to, nor make contact with, fan housing.
The installation of a fan directly under a cold air grille is not recommended
on account of the noise objection. See also Chapter 18.
AIR WASHERS AND FILTERS
Washers for residence systems may be provided in separate housings
to be installed on the inlet or outlet side of the fan, or they may be
integral with the fan construction. They operate at water pressures of
from 10 to 30 Ib and use two or more spray nozzles for washing and
humidification. The sprays should be adjusted to completely cover the
air passages.
Washers are usually controlled by solenoid valves wired in parallel with
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CHAPTER 23 — MECHANICAL WARM AIR FURNACE SYSTEMS
the fan motor. The water supply may, in turn, be controlled by a
humidity-controlling device located in one of the living rooms, so that the
washer will operate at all times when the fan is in operation, unless the
relative humidity should rise beyond a desirable percentage. Washers
used in connection with commercial or heavy duty plants should be a
regulation type of commercial washer.
There are many satisfactory types of filters on the market. These
include dry filters, viscous filters, oil filters and other types, some of which
must be cleaned, some of which must be cleaned and recharged with oil,
and some of which are inexpensive and may be discarded when they
become dirty, and replaced with new ones.
The resistance of a filter must be considered in the design of the system
since the resistance rises rapidly as the filter becomes dirty, thus im-
pairing the heating efficiency of the furnace, in fact, endangering the life
of the furnace itself. Manufacturers' ratings of filters must be carefully
regarded, and ample filter area must be provided. Filters must be
replaced or cleaned when dirty. See also Chapter 16.
COOLING METHODS
Some cooling may be obtained under certain conditions by the use of
basement air. A more positive cooling effect may be obtained through air
washers where the temperature of the water is sufficiently low (55 F or
lower), and where a sufficient volume of water can be provided. Unless
the water is below the dew point temperature of the indoor air at the time
the washer is started, both the relative and absolute humidities will be
somewhat increased.
Coils of copper finned tubing through which cold water is pumped are
available for cooling. They require less space than air washers and have
the advantage that no moisture is added to 'the air when the temperature
of the water rises above the dew point. Ample coil surface is necessary
with this type of cooling.
It is thoroughly feasible to use ice or mechanical refrigeration in con-
nection with the fan and duct system for the heating installation, and to
cool the building by this method, provided the building is reasonably
well constructed and insulated. Windows and doors should be tight, and
awnings should be supplied on the sunny side of the building. See also
Chapters 9 and 10.
Study of these problems sponsored by the AMERICAN SOCIETY OF
HEATING AND VENTILATING ENGINEERS in cooperation with the National
Warm Air Heating Association is in progress at the University of Illinois.
The following conclusions may be drawn from the studies thus far com-
pleted, subject to the limitations of the conditions under which the tests
were run1:
1. An uninsulated building of ordinary residential type may require the equivalent of
three tons of ice in 24 hours on days when the maximum outdoor temperature reaches
100 F if an effective temperature of approximately 72 deg is maintained indoors.
*See A.S.H.V.E. research paper entitled Study of Summer Cooling in the Research Residence at the
University of Illinois, by A. P. Kratz and S. Konzo (A. S. H, V. E. Journal Section Heating, Piling an$ Air
Conditioning, February, 1933).
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
2. The use of awnings at all windows in east, south, and west exposures may result in
savings of from 20 to 30 per cent in the required cooling load.
3. The cooling load per degree difference in temperature is not constant but increases
as the outdoor temperature increases.
4. The heat lag of the building complicates the estimation of the cooling load under
any specified conditions and makes such estimates, based on the usual methods of com-
putation, of doubtful value.
5. The seasonal cooling requirements are extremely variable from year to year, and
the ratio between the degree-hours of any two seasons occurring within a 10-year period
may be as high as 7.5 to 1. Hence an average value of the degree-hours cooling per
season is comparatively meaningless.
6. The results of the tests suggest the use of a fan at night either to provide more
comfortable conditions during the following day without provision for cooling, or to
reduce the load required for cooling during the following day. Experience has shown that
the volume of air required for cooling, depending upon the climate and the construction
of the building, must usually be from 50 to 100 per cent greater than^that required for
heating. If the size of the fan is based upon the summer requirement, its output may be
reduced sufficiently to meet winter heating needs.
7. Attic exhaust fans are becoming popular adjuncts for night duty. (See Chapter 13.)
DUCT DESIGN
The ducts may be either round or rectangular. Rectangular ducts
should be as nearly square as possible; the width should not be greater
than four times the breadth. The radii of elbows should be not less than
]/OL UMUL
FIG. 4. THREE TYPES OF DAMPERS COMMONLY USED FOR TRUNK AND INDIVIDUAL
DUCT SYSTEMS
one and one-half times the pipe diameter for round pipes, or the equiva-
lent round pipe size in the case of rectangular ducts.
The ducts or piping may be designed either as a trunk line system or as
a system of individual ducts from the furnace casing to each register. The
engineering problems incident to the design of a trunk line system are
somewhat more difficult than for the individual duct system. The trunk
line system is generally a tailor-made job, whereas the individual duct
system with which either round or square ducts may be used may fre-
quently be assembled from stock materials and thus installed at a con-
siderable saving. Individual ducts may frequently be grouped to simulate
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CHAPTER 23 — MECHANICAL WARM AIR FURNACE SYSTEMS
a trunk duct system in appearance. The design of ducts for air flow is
described in Chapter 20.
Dampers
Suitable dampers are essential to any trunk or Individual duct system,
as it is virtually impossible to so lay out a system that it will be absolutely
in balance without the use of dampers. Special care must be used in the
design of any system to avoid turbulence and to minimize resistance.
Sharp elbows, angles, and offsets should be avoided. See Figs. 1 and 2f
Chapter 20.
Three types of dampers are commonly used in trunk and individual
duct systems. Volume dampers are used to completely cut off or reduce
the flow through pipes. (See A and 2?, Fig. 4.) Splitter dampers are used
where a branch is taken off from a main trunk. (See C, Fig. 4.) Squeeze
dampers are used for adjusting the volume of air flow and resistance
through a given duct. (See D, Fig. 4.) It is essential that a damper be
provided for each main or duct branch. A positive locking device should
be used with each type of damper.
Supply and Return Air Registers
Supply registers located in the floor are effective, but as they require
frequent attention to keep them clean they should be avoided where
another effective register location can be found. Unless registers located
in the baseboard are well proportioned and designed to harmonize with
the trim, they may be unsightly. Registers which are located in side walls
above the baseboard or in the ceiling should be of an effective air-diffusing
type. All registers should be sealed against leakage around the borders
or margins.
Velocities through registers may be reduced by the use of registers
FIG. 5.
DIFFUSERS IN TRANSITION FITTINGS TO EQUALIZE VELOCITIES
THROUGH REGISTER FACES
larger than the connecting pipes. Some suggestions for equalizing veloci-
ties over the face area of the register by means of diffusers are illustrated
in Fig. 5. Merely to use a larger register may not result in materially
reduced velocities unless such diffusers are used.
Care should be exercised in making the connection between the supply
register and its box to prevent streaking of the wall. All warm air
registers should be equipped with dampers or, better, with diffuser
dampers which may be used to direct air currents in such a way that they
will not be objectionable. (See Chapter 19.)
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
ko £
382
CHAPTER 2£— MECHANICAL WARM AIR FURNACE SYSTEMS
CONTROLS
Air stratification, high bonnet temperatures, excessive flue gas tem-
peratures, and heat overrun or lag in the system can be largely elimi-
nated through proper care in the planning and installation of the control
system. The essential requirements of the control are:
1. To keep the fire burning when using solid fuel regardless of the weather.
2. To avoid excessive bonnet temperatures with resultant radiant heat losses into the
basement.
3. To avoid the overheating of certain rooms through gravity action during off
periods of blower operation.
4. To have a sufficient supply of heat available at all times to avoid lag when the
room thermostat calls for heat.
5. To prevent cold air delivery when heat supply is insufficient.
6. To avoid heat loss through the chimney by keeping stack temperatures low.
7. To provide quick response to the thermostat, with protection against overrun.
8. To provide for humidity control.
9. To provide a means of summer control of cooling.
10. To protect against fire hazards.
The following controls are desirable:
1. A thermostat located at a point where maximum fluctuation in temperature can be
expected, in order to secure frequent operation of fans, drafts, and burners. This location
would be near an outside wall but not upon it7 in a sun room, or in a room with some
unusual exposure. The thermostat, of course, should not be located where it will be
affected by direct radiant heat from the sun or from a fireplace, or by direct heat from
any warm air duct or register.
2. A furnacestat located in the bonnet to permit blower operation only between the
temperatures of 100 F and 150 F. In certain extreme cases it may be necessary, or
weather conditions may make it advisable, to adjust the high limit to a higher tempera-
ture than that given. Another location sometimes used for the furnacestat is in the main
duct near the frame opening from the bonnet.
3. A protective limit control located in the bonnet to shut down the system inde-
pendently of the thermostat if the bonnet temperature exceeds 225 F.
4. On oil and §as burner installations, a control is usually included which will shut
down the system if the fire goes out or if there is a failure of the ignition system.
5. A humidistat to regulate the moisture supplied to the rooms.
6. On automatic stoker installations, a control is usually included which will start
the operation regardless of thermostat settings whenever the bonnet temperature
indicates that the fire is dying.
While it is usually all right to start and stop the fan in residential con-
trol work and in auditoriums and other places where many people may
gather, the fan should as a rule be allowed to run continuously and the
control should be cared for in other ways.
SELECTING THE FURNACE
The following formula may be used to compute the grate area of a
residence "furnace, assuming a ratio of heating surface to grate area
of 20 to 1 :
7-7-.
G = FXCXE (1)
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
o o
IB
SSRHg
gj &• tH M ~
sSESp
^Se5
w B g «« w w
w J3 S iJ S a:
£5^ O^ S g
8O. W *4 ffl
nS'S^g
ili<§5
384
CHAPTER 23 — MECHANICAL WARM AIR FURNACE SYSTEMS
where
G = required grate area, square feet.
H = total heat loss from building, Btu per hour.
F = calorific value of coal, Btu per pound.
C — combustion rate in pounds of fuel per square foot of grate per hour.
E — furnace efficiency based on heat available at register faces.
In practice it is customary to use the following constants :
F = 13,000 (For specific values, see Table 1, Chapter 27).
C = 5 to 10 Ib (Use 8 Ib as maximum in residence work).
E =* 55 per cent to 65 per cent depending on fuel burned. Lower efficiency must
be used with highly volatile solid fuel.
Where ratio of heating surface to grate area is less or greater than 20 to
1, deduct or add 2 per cent from or to rating of furnace for each unit
decrease or increase in ratio, as the case may be. The foregoing procedure
for determining the size of the furnace to be used applies to continuously
heated buildings.
Although intermittently heated buildings usually have their heat losses
computed according to the standard rules for determining such losses,
these rules do not take into account the heat which will be absorbed by
the cold material of the building after the air is raised in temperature.
This heat absorption must be added to the normal heat loss of the building
to determine the load which the heating plant must carry through the
warming-up process. It is customary to increase the normal heat loss
figure by from 50 to 150 per cent depending upon the heat capacity of the
construction material, the higher percentage applying to materials of
high heat capacity such as concrete and brick. Fan furnace systems are
well adapted for heating intermittently heated buildings as these systems
do not require the warming of intermediate piping, radiators, or con-
vectors, the generation of steam, or the heating of hot water.
Follow the same methods for an oil furnace as for coal where a con-
version unit is to be used, making sure that the ratio of heating surface to
grate area exceeds 20 to 1. If it does not, a size larger furnace should be
selected. Use the manufacturers' Btu ratings of furnaces designed for
exclusive use with oil, and select a burner with liberal excess capacity.
The selection of the proper size gas furnace for a constantly heated
building can be easily made by using the following American Gas Associa-
tion formula :
* = <§ (2)
where
H = total heat loss from building in Btu per hour.
R = official A.G.A. output rating of the furnace in Btu per hour.
In the case of converted warm air furnaces a slightly different procedure
is necessary, as the Btu input to the conversion burner must be selected
rather than the furnace output. The proper sizing may be done by means
of the following formula:
/ = 1.56H (3)
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
where '
I = Btu per hour input.
The factor 1.56 is the multiplier necessary to care for a 10 per cent heat
loss in the distributing ducts and an efficiency of 70 per cent in the con-
version burner.
SELECTING THE FAN
Choose a fan which, according to its manufacturer's rating, is capable
of delivering a volume of air, expressed in cubic feet per minute, against
a frictional resistance, expressed in inches of water, computed by adding
together the following items:
1. The frictional resistance of a warm air trunk or leader.
2. The frictional resistance of a return air trunk or duct.
3. The resistance to the flow of total volume of air through the furnace casing or hood,
which is usually considered from 0.10 to 0.15 inches of water.
4. The frictional resistance through any other accessories, such as washers or niters.
5. A factor of safety of 10 per cent of the resistance calculated above.
HUMIDITY
Mechanical warm air systems offer an excellent means of proportioning
and distributing moisture-bearing air; consequently, during the winter
months humidifiers may be employed to deliver water vapor to the fan-
driven air stream in proper amounts to produce a more humid atmos-
phere, with increased comfort for people and increased life for household
furnishings. Temperatures and relative humidities should be governed
within the limits of the generally accepted standards. See Chapters 2 and
3 for more detailed information on this point.
In earlier types of furnaces, water evaporating pans were usually placed
in the cool portions of the air stream, but modern types usually locate
them in air which has been heated by contact with the heating surfaces.
To change water into vapor capable of being carried in an air stream as
part of the -mixture, about 1000 Btu per pound are required. Without
the addition of this heat, termed the latent heat of evaporation, water,
injected intathe air will be carried along in the form of tiny globules until
it falls out of the stream or is deposited upon some surface. .
Furthermore, when dry air is in contact with water for a sufficient
length of time without the presence of a sizable body of water or a source
other than air from which this latent heat of evaporation can be taken,
such heat is supplied from the air. There is, therefore, a trend in present
practice toward heating the water in addition to heating the air. Equip-
ment for doing this may make use of sprays, or it may take the form of
water circulating coils placed within the combustion chamber and con-
nected by pipes to the humidifier pans where a constant water level is
maintained by some separate float device. (See Chapter 11.)
PROVISION FOR COOLING SYSTEM
If the system is to be used for cooling, the following provisions should
be made:
CHAPTER 23 — MECHANICAL WARM AIR FURNACE SYSTEMS '
1. Where cooling is to be secured through air circulation only:
a. Provide for an increase of 50 to 100 per cent in fan capacity through multi-speed
pulleys or other means,
b. If basement air or outside night air is to be used, provide suitable basement
opening in duct system, or outdoor air intake,
2. Where water below 55 F or artificial refrigeration or ice is to be used:
a. Provide outside air duct for circulation of cool night air for economy.
b. Make provision in return duct system for cooling unit.
c. Make provision for control of the fan speed, during winter operation, to give
a sufficient and draftless air movement.
HEAVY DUTY FAN FURNACES
Fan furnaces for large commercial and industrial buildings are available
in sizes ranging from 400,000 to 3,000,000 Btu per hour per unit. Heavy
duty heaters may be arranged in combinations of one or more units in a
battery. A few possible arrangements are shown in Figs. 6 to 13, in-,
elusive.
Most manufacturers of heavy duty furnaces rate their furnaces in Btu
per hour and also in the number of square feet of heating surface. Con-
servative practice indicates that at no time in the heating-up period
should the furnace surface be required to emit more than an average of
3500 Btu per square foot. A higher rate of heat emission tends to increase
the heat loss up the chimney, and raise fuel consumption, to shorten the
life of the furnace, and to overheat the air, The ratio of heating surface
to grate area on furnaces for this type of work should never be less than
30 to 1 and as indicated previously may run as high as 50 to 1.
Control of temperature is secured through (1) controlling the quantity
of heated air entering the room, (2) using mixing dampers, or (3) regu-
lating the fuel supply.
The design of heavy duty fan furnace heating systems is in many
respects similar to that of the central fan heating systems described in
Chapter 22. Ducts are designed by the method outlined in Chapter 20.
PROBLEMS IN PRACTICE
1 • Why do furnaces designed to burn bituminous coal, oil, or gas require
larger combustion spaces than those designed for anthracite?
Anthracite burns largely as fixed carbon whereas gas and oil burn as gases, and as much
as 50 per cent of bituminous coal burns as a gas. Ample space must be provided for the
intimate mixture of these gases with the oxygen of the air to secure proper combustion.
2 • A furnace has the following dimensions: Grate diameter, 24 in.; casing
diameter for gravity air flow, 56 in.; combustion chamber diameter, 30 in.
What is the unobstructed area required for passage of ah* across the heating
surface when a motor-driven hlower, operating at an outlet velocity of 1200 fpm,
delivers 1600 cfm into the casing near its bottom?
For residence applications using small blowers, an air outlet velocity of about one third
of the blower" outlet velocity is considered good practice1.
387
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
1 200
Air-pass velocity = — •« — = 400 fpm.
o
Air-pass area = — j— = 4 sq ft = 576 sq in.
3 • In Question 2 what would be the gap between the chamber and the baffle
when the chamber is centered in the casing?
Area of combustion chamber (30-in. diam) 706.9 sq in.
Area of air pass 576.0 sq in.
Total area 1282.9 sq in.
The diameter of a circle with an area of 1282.9 sq in. is 40.4 in. One half of the difference
between the diameters is the amount of gap.
Gap = — : — H- — = 5.2 in. = approximately 5K in.
* fJ
4 • Why should secondary surface be designed for easy cleaning?
If the combustion is not perfect, soot is formed immediately above the fire and is apt
to form a deposit on the secondary surface from which it should be removed. If the
secondary surface is so designed that there are horizontal passages, fine gray ash will
settle out in these to form an insulation between the hot gases of combustion and the
metal of the furnace; consequently, these should be readily cleaned. If the passages are
vertical they are largely self-cleaning of ash, but provision should be made for easy and
thorough cleaning of the collection chamber below them.
5 • Why is baffling inside the casing necessary on fan systems?
Because the movement of air is independent of its temperature, air must be guided by
baffles of one form or another to bring it in contact with the hot surfaces so it will not
pass through the casing unheated. On the other hand, if the air is held against a hot
surface too long it might become overheated, for the average register temperature on a
fanjsystem should not exceed 120 F.
6 • Why do buildings which are intermittently used require more heating
capacity than buildings constantly used?
Between heating periods the intermittently used building is allowed to cool down. All
of the material in the building loses heat, and before the building can be reheated to a
comfortable temperature this material must also be reheated.
7 • What practical points should be observed in designing a fan system in order
to eliminate noise?
a>. Use a large fan so it can be run at slow speed.
b. Set the fan and motor on a solid foundation.
c. Insulate the fan and motor from the foundation with rubber, cork, or other springy
material according to the principles given in Chapter 18, provided, of course, that such
insulation is of value.
d. See that the air velocity is not too high in the ducts. Properly designed splitters in
the elbows will avoid high velocities at the turns in cases where the velocity through the
ducts themselves is not too high.
e~ Use canvas connections between the ducts and any running equipment.
/. Be sure the ducts have a relatively smooth interior and are rigid.
388
Chapter 24
GRAVITY WARM AIR FURNACE
SYSTEMS
Procedure for Design, Estimating Heating Requirements, Sizes of
Leader Pipes, Proportioning Wall Stacks, Register Sizes, Recircu-
lating Ducts and Grilles, Return Connection to Furnace, Furnace
Capacity, Examples, Booster Fans
WARM air heating systems of the gravity type are described in this
chapter1, and those of the mechanical type are described in Chapter
23. In the gravity type, the motive head producing flow depends upon
the difference in weight between the heated air leaving the top of the
casing and the cooled air entering the bottom of the casing, while in the
mechanical type a fan may supply all or part of the motive head. Booster
fans are often used in conjunction with gravity-designed systems to
increase air circulation.
In general, a warm-air furnace heating plant consists of a fuel-burning
furnace or heater, enclosed in a casing of sheet metal or brick, which is
placed in the basement of the building. The heated air, taken from the
top or sides near the top of the furnace casing, is distributed to the
various rooms of the building through sheet metal warm-air pipes. The
warm-air pipes in the basement are known as leaders, and the vertical
warm-air pipes which are run in the inside partitions of the building are
called stacks. The heated air is finally discharged into the rooms through
registers which are set in register boxes placed either in the floor or in
the side wall, usually at or near the baseboard.
The air supply to the furnace may be taken (1)" entirely from inside
the building through one or more recirculating ducts, (2) entirely from
outside the building, in which case no air is recirculated, or (3) through a
combination of the inside and the outside air supply systems. \
PROCEDURE FOR DESIGN
The design of a furnace heating system involves the determination
of the following items:
1. Heat loss in Btu from each room in the building.
2. Area and diameter in inches of warm-air pipes in basement (known as leaders).
3. Area and dimensions in inches of vertical pipes (known as wall stacks),
4. Free and gross area and dimensions in inches of warm-air registers,
5. Area and dimensions of recirculating or outside air ducts, in inches.
6. Free and gross area and dimensions in inches of recirculating registers.
JAn figures and much of the engineering data which follow are from Bulletins No. 141, 188 and 189,
Warm Air Furnaces and Heating Systems, Part II, by Professor A. C. Willard, A. P. Kratz, and V. SL
Day, Engineering Experiment Station, University of Illinois.
389
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
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CHAPTER 24 — GRAVITY WARM AIR FURNACE SYSTEMS
7. Size of furnace necessary to supply the warm air required to overcome the heat
loss from the building. This size should include square inches of leader pipe area which
the furnace must supply. It is also desirable to call for a minimum bottom fire-pot
diameter in inches, which is the nominal grate diameter. •
8. Area and dimensions in inches of chimney and smoke pipe. If an unlined chimney
is to be used, that fact should be made clear.
The heat loss calculations should be made in accordance with the
procedure outlined in Chapter 7, taking into consideration the trans-
mission losses as well as the infiltration losses/
SIZES OF LEADER PIPES
In a gravity circulating warm-air furnace system the size of the leader
to a given room depends upon the temperature of the warm air entering
the room at the register. A reasonable air temperature at the registers
must, therefore, be chosen before the system can be designed. The
National Warm Air Heating Association has approved an air temperature
of 175 F at the registers as satisfactory for design purposes. At this tem-
perature, the heat-carrying capacity (heat available above 70 F) per
square inch of leader pipe per hour for first, second or third floors is shown
by Fig. 1 at 175 F to be 105, 170 and 208 Btu, respectively. For average
calculations, the values 111, 166 and 200 will simplify the work and may
be satisfactorily substituted for these heat-carrying capacities. If H
represents the total heat to be supplied any room, the resulting equations
are:
Leader areas for first floor, square inches — — = approximately 0.009IT (1)
H
Leader areas for second floor, square inches = r^r = approximately 0.006H (2)
rr
Leader areas for third floor, square inches = ^rr » approximately 0.005J3" (3)
In designing for a lower warm-air register temperature, say 160 F, the
factors 111, 166 and 200 become 80, 140 and 166 (Fig. 1 at 160 F), and
the resulting equations are:
TT
Leader areas for first floor, square inches = -^r- = approximately 0.012-ET (4)
•rr
Leader areas for second floor, square inches = -rrr — approximately 0.0075' (5)
Leader areas for third floor, square inches = r^ = approximately O.OO&H (6)
loo
These equations are applicable to straight leaders from 6 to 8 ft in
length. Longer leaders must be very thoroughly covered or else the
vertical stacks must be increased in area as discussed under wall stacks.
If some provision is not made for these longer leaders, the air tempera-
ture may be much lower than anticipated and the room will not be
properly heated.
While Fig. 1 takes care of the drop in temperature in straight leaders
up to 8 ft in length connected to stacks having about 75 per cent of the
391
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
area of the leader, the designer must make allowances for all other
conditions. The temperature drop in leaders of various lengths at three
different register temperatures is shown in Fig. 2, and should be used to
obtain new register temperatures, lower than 175 F, on which to base
selections from the curves of Fig. 1, and thereby new constants for
Equations 1, 2 and 3.
Leader sizes should in general be not less than those obtained by
Equations 1 to 3 nor should leaders less than 8 in. in diameter be used. It
is not considered good commercial practice to specify diameters except
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FIG. 3. RELATIVE HEATING EFFECT OF STACKS AT CONSTANT HEAT
INPUT TO FURNACE
Note. — Exterior surface of all ducts is bright tin except at joints
' • where asbestos sealing strips are used.
in whole inches. The tops of all leaders should be at the same elevation as
they leave the furnace bonnet, and from this point there should be a
uniform up-grade of 1 in. per foot of run in all cases. Leaders over 12 ft
in length are to be avoided or should receive very special attention.
PROPORTIONING WALL STACKS
The wall stack for an upper floor should be made not less than 70
per cent of the area of the leader which has been selected from Fig. 1.
So long as the leader is short and straight as was the case for Fig. 1,
392
CHAPTER 24 — GRAVITY WARM AIR FURNACE SYSTEMS
such a practice is probably justified, since the loss (Fig. 3) in capacity
occasioned by the smaller stack is not very serious for stacks having
areas in excess of 70 per cent of the leader area. For leaders over 8 ft
in length or for leaders which are not straight, the ratio of stack area to
leader area should be greater than 70 per cent in order to offset the
greater temperature losses (Fig. 2) in the longer leader. In gravity
circulating systems, this stack to leader area ratio is a very important
consideration. Specific data for a great variety of cases are presented
in Figs. 4 and 5 and the designer should check the stack to leader com-
binations with the nearest comparable case as shown in these figures.
Any second-floor stack supplying heat to a room whose heat loss is 9,000
Btu or more (see Figs. 4 and 5 which show that high temperatures
are necessary if rooms of more than 9,000 Btu requirement are heated by
one stack each in 4-in. studding) should be run within 6-in. studded walls
or should have multiple stacks. Stack sections, wherever possible, should
be changed from the thin rectangular to the more nearly square shape.
REGISTER SIZES
The registers used for discharging warm air into the rooms should have
free or net area not less than the area of the leader in the same run of
piping. The free area should be at least 70 per cent of the gross area
of the register. No upper-floor register should be wider horizontally
than the wall stack, and it should be placed either in the baseboard or
side wall, if this can be done without the use of offsets. First-floor registers
may be of the baseboard or floor type, with the former location preferred.
RECIRCULATING DUCTS AND GRILLES
The ducts through which air is returned to the furnace should be
designed to minimize friction and turbulence. They should be of ample
area, in excess of the total area of warm-air pipes, and at all points where
the air stream must change direction or shape, streamline fittings should
be employed. Horizontal ducts should pitch at least J^ in. per foot
upward from the furnace.
The recirculating grilles (or registers) should have a free area at least
equal to the ducts to which they connect, and their free area should
never be less than 50 per cent of their gross area.
The location and number of return grilles will depend on the size, details
and exposure of the house. Small compactly built houses may frequently
be adequately served by a single return effectively placed in a central hall.
More often it is desirable to have two or more returns, provided, however,
that in two-story residences one return must be placed to effectively
receive the cold air returning by way of the stairs.
Where a divided system of two or more returns is used, the grilles
must be placed to serve the maximum area of cold wall or windows.
Thus in rooms having only small windows the grille should be brought
as close to the furnace as possible, but if the room has a bay window,
French doors, or other large sources of cooling or leakage of cold air, the
grille should be placed close by, so as to collect the cool air and prevent
drafts. When long ducts of this type are employed they must be made
393
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
oversize and favored in every way. This precaution is particularly
important when long ducts and short ducts are used in the same system.
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The long ducts must be oversize, if they are to operate satisfactorily in
parallel with short ducts.
Return ducts from upstairs rooms may be necessary in apartments
or other spaces closed off or badly exposed. Metal linings are advisable
in such ducts. It is important that these ducts be free from unnecessary
394
CHAPTER 24 — GRAVITY WARM AIR FURNACE SYSTEMS
friction and turbulence, and that they be located to prevent preheating
of the air before it reaches the furnace.
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Return Connection to Furnace
' Circulation is accelerated if the drop to the furnace is through a round
inclined pipe with, say, two 45-deg elbows rather than through a vertical
drop and two 90-deg elbows. The top of the shoe should never enter
395
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
the casing above the level of the grate in the furnace. To accomplish
this the shoe must be wide.
Tests of six different systems of cold air returns, Fig. 6, made at the
University of Illinois2, resulted in the following conclusions:
1. In general, somewhat better room temperature conditions may be obtained by
returning the air from positions near the cold walls.
2. Friction and turbulence in elaborate return duct systems retard the flow of air,
and may seriously reduce furnace efficiency, and lessen the advantages of such a design.
3. The cross-sectional duct area is not the only measure of effectiveness. Friction
and turbulence may operate to make the air flow out of all proportion to the various
duct areas.
Are ft of /ncrss? &>/* t?v
Area of Mvrrm-o'/s* p/pes S3S *s<f //? frpes no?
FIG. 6. ARRANGEMENT OF COLD AIR RETURNS FOR Six INSTALLATIONS
FURNACE CAPACITY
The size of furnace should, of course, be such as will provide the
necessary air heating capacity, usually expressed in square inches of
leader pipe area, and at the same time provide a grate of the proper
area to burn the necessary fuel at a reasonable chimney draft. The total
leader pipe area required is easily obtained by finding the sum of the
leader pipe areas as already designated.
The grate area will depend on several factors of which four are very
important. First of all, the air temperature at the register for which
the plant has been designed must be determined. Usually, this tempera-
ture is taken as 175 F. Second in importance is the combustion rate,
which must always correspond with the register air temperature, as is shown
by reference to a set of typical furnace performance curves (Fig. 7) for a
cast-iron circular radiator furnace with a 23-in. diameter grate and 50-in.
diameter casing. The conditions shown on these curves which seem to
a Investigation of Warm-Air Furnaces and Heating Systems, Part N, by A. C. Willard, A. P. Kratz and
V. S. Day (University of Illinois Engineering Experiment Station Bulletin No. 189).
CHAPTER 24 — GRAVITY WARM AIR FURNACE SYSTEMS
approximate nearest to the 175 F register warm-air temperature are:
combustion rate, 7 Ib; warm-air register temperature, 173 F; efficiency of
the furnace, 58.5 per cent. The third factor is efficiency, which, in turn, is
a function of the combustion rate varying with it as shown by the effi-
ciency curve of Fig. 7. The fourth factor is the heat value per pound of
fuel burned, which was 12,790 Btu. This is not shown on the curves since
it was constant for all combustion rates.
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FIG. 7. TYPICAL PERFORMANCE CURVES FOR A WARM AIR FURNACE AND INSTALLATION
IN A THREE STORY TEN LEADER PLANT, OPERATING ON RECIRCULATED AIR
From the relation existing among these factors it is found (Fig. 7) that
the capacity of the furnace under test is 147,750 Btu per hour for the total
grate, which gives the capacity at the furnace bonnet per square foot of
grate as 51,200 Btu and per square inch of grate as 356 Btu per hour.
Suppose it is desired to select a furnace to deliver air to the rooms at a
register temperature approximating 160 F rather than 175 F. Referring
to the curves, the relation is: combustion rate, 5.5 Ib; register warm-air
temperature, 160 F ; and efficiency of the furnace, 62 per cent. Under this
condition the capacity of the furnace at the furnace bonnet per square
foot of grate area is 43,200 Btu per hour, and per square inch of grate it is
300 Btu per hour. From these performance values^ the grate area for any
397
AMERICAN SOCIETY of HEATING dnJ VENTILATING ENGINEERS GUIDE, 1935
FIG. 8. BASEMENT PLAN, RESEARCH RESIDENCE
FIG, 9. FIRST-FLOOR PLAN, RESEARCH RESIDENCE
398
CHAPTER 24 — GRAVITY WARM AIR FURNACE SYSTEMS
plant requirement (allowing 20 per cent heat loss between furnace and
registers) will be:
1 2 H
Grate area (175 F register temperature), square inches = •• ' = 0.0034H" (7)
oOD
Grate area (160 F), square inches - ^^ =0.00405" (8)
oUU
Here H = Btu heat loss from the entire house per hour = summation
of all room losses H i + H% + etc. + the Btu necessary to heat the fresh
air, if any, at intake. This fresh air loss in Btu per hour will be approxi-
mately 1.27 times the cubic feet of air admitted through the intake per
hour on a zero day. For systems which recirculate all the air this value
will be zero. For systems which have a fresh air intake, controlled by
damper, this value might well be approximated, since this loss will
probably be reduced to a minimum on a zero day. Assume for such cases
that the building loss is increased by 25 per cent, and that there is the
usual 20 per cent loss between furnace and registers.
It is not always possible to obtain performance curves, and the fol-
lowing method is suggested as being a close check. An addition of 2 per
cent of the furnace capacity is proposed for each unit that the heating
surface to grate area ratio of the furnace exceeds 20. This addition is
based on tests made at the University of Illinois, of four types of furnaces
having various ratios of heating surface to grate area.
Let E « efficiency of the furnace.
/ = fuel value of the coal, Btu per pound.
p = pounds of coal burned per square foot of grate per hour.
R = ratio of heating surface to grate area.
H ~ total heat requirements of the house.
1 2 X 111 H
Grate area, square inches = £ . f 1 + Q 02 (.R ~ 20) ] f°r al* insi(*e ain ^
For coal having a heat value of 12,000 Btu, and a furnace having 60 per
cent efficiency, with 6 Ib of coal burned per square foot of grate per hour,
and 20 sq ft of heating surface for 1 sq ft of grate, this becomes :
1 2 X 144 H
Grate area, square inches * Q 60 ' X 12 000 X 6 f°f a11 insi<le air'
and for another furnace having 24 sq ft of heating surface for 1 sq ft
of grate the expression is
. . 1.2 X 144 H ,in
Grate area, square inches = 0.60 X 12,000 X 6 [1+ 0.02 (24 ~- 20)] (11)
The air temperatures at the registers corresponding to the conditions
of Equation 11 would be approximately 165 F, and for 175 F and 12,000
Btu the combustion rate would be about 7.5 Ib with an efficiency of
57 per cent, using the curves of Fig. 7 as a guide.
TYPICAL DESIGN
The application of the preceding data to an actual example may be of
assistance to the designer. Figs. 8, 9, 10 and 11 represent the plans of
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
FIG. 10. SECOND-FLOOR PLAN, RESEARCH RESIDENCE
FIG. 11. THIRD-FLOOR PLAN, RESEARCH RESIDENCE
'400
CHAPTER 24 — GRAVITY WARM AIR FURNACE SYSTEMS
the Warm Air Research Residence of the National Warm Air Heating
Association erected at the University of Illinois3.
Leaders, Stacks and Registers. (Direct Method)
Living Room, 1st floor:
17,250 -r- 111 = 155 sq in. leader area. See summary, Table 1; also example under
Standard Code4, Art. 3, Basis of Working Rules for Pipes.
Leader diameter = 14 in.
Register size = 155 sq in. net area. Gross area = net area -f- 0.7 = 14 in. X 16 in.
Owner's Room, 2nd floor:
15,030 -r- 167 = 90 sq in. leader area. See Summary Table; also example under
Standard Code4, Art. 3, Basis of Working Rules for Pipes.
Leader diameter = 11.4, say 12 in.
Stack area = 0.7 X 90 = 63 sq in. = say 5 in. X 12 in.
Register area = 90 sq in. net area. Gross area = net area -f- 0.7 = 12 X 12
or 12 in. X 14 in.
In like manner the leaders, stacks and registers are calculated for each
room in the house.
Leaders, Stacks and Registers. (Code 4 Method. See Art. 3, Sec. 1, 2, 3.)
Living Room (Glass - 90, Net wall = 405, Cubic contents = 2405)
T - / 90 . 405 , 2405 \ n 1KK .
Leader = (^_ + — + w J 9 = 155 sq m.
Register, same as Direct Method.
Owner's Room (Glass = 68, Net wall = 394, Cubic contents = 2275)
T . / 68 , 394 , 2275
Leader - ^_+_ +
* Stack and Register, same as Direct Method.
Assuming all air recirculated, the minimum furnace for the plant
will be :
Grate area = 0.0034 X 132,370 = 450 sq in. « 24 in. diameter at 175 F
register temperature. (Equation 7)
Grate area « 0.0040 X 132,370 « 530 sq in. = 26 in. diameter at 160 F
register temperature. (Equation 8)
If provision should be made for certain outside air circulation, then
increase the building heat loss by, say 25 per cent and obtain by Equation
7 a 27-in. grate and by Equations 8 and 10 a 29-in. grate.
Experiments at the University of Illinois5 have shown that the capacity
of a furnace may be increased nearly three times by an adequate fan,
3Plans used with permission. Bathroom on third floor not heated.
^Standard Code Regulating the Installation of Gravity Warm Air Heating Systems in Residences.
This code has been sponsored by the National Warm Air Heating Association, the National Association of
Sheet Metal Contractors, and the AMERICAN SOCIETY OF HEATING AND VENTILATING ENGINEERS. It is
recommended that the installation of all gravity warm air heating systems in residences be governed by
the provisions of this code, the eighth edition of which may be obtained from the National Warm Air Heating
Association, 3440 A.I.U. Building, Columbus, Ohio.
*See University of Illinois Eng. Exp. Sla. Bulletin No. 120, p. 129.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
with a constant register or delivery temperature maintained, provided
that the rate of fuel consumption can be increased to provide the necessary
heat. In other words, the capacity of a forced circulation systern is limited
by the ability of the chimney to produce a sufficient draft.
TABLE 1. SUMMARY OF DATA APPLIED TO WARM AIR RESEARCH RESIDENCE
Rooms
From
Chapter 7
Estimating
Heat Losses
Btu
Heat Losses
H
Leader
Area
SQ In.
Stack Area
Sq In.
0.7 X LA
Leader
Diameter
Inches
Stack
Size
Net
Register
Size
Gross
First Floor
Livinsr .
17250
« 0.0091?
155
14
14 X 16
AwA V lllg
Dining—.
Kitchen
Sun
6810
2300
9210
25710
61
21
83
230
—
9
8
11 or 12
Two 12
8X12
8 X 10
12 X14
Two 12 X 14
Hall and stair
Second Floor
Owner's
S. W. Bed......
Bath
N. Bed
12570
15030
9800
2450
14800
113
» 0.006H
90
59
15
89
63
41
10
62
12
11 or 12
9
8
11 or 12
5X 12
3J^X 12
3X 10
5 X 12
12 X 14
12 X 14
8X12
8 X 10
12 X 14
Third Floor
E. Bed
W. Bed
8220
8220
- 0.005H
41
41
29
29
8
8
3X 10
3 X 10
8X10
8 X 10
BOOSTER FANS
Booster fans often may be arranged to operate when gas or oil burners
are running and to stop automatically when the burners shut down. The
booster equipment is most effective in increasing output at low operating
temperatures. According to tests, efficiencies may be advanced from 60
per cent for gravity to 70 per cent with boosters at low operating tem-
peratures, but at high operating temperatures gravity and booster
efficiencies are almost identical6.
•See University of Illinois Bng. Exp. Sta. Bulletin No. 141, p. 79.
PROBLEMS IN PRACTICE
1 • A facet story dining room has a calculated heat loss of 12,000 Btu per hour.
a. What size leader pipe should he used for 175 F register air temperature?
b. "What size register?
12 000
a. Leader area =* ~~TTi — ~ 108.1 sq in. Use leader with diameter of 12 in.
1). Register gross area
108
•JT-= — 154 sq in. Use 12 in. by 14 in. register.
402
CHAPTER 24 — GRAVITY WARM AIR FURNACE SYSTEMS
2 • A third-story bedroom has a calculated heat loss of 12,000 Btu per hour.
a. What size leader pipe should be used for a 175 F register air temperature?
b. What size stack?
c. What size register?
a. Leader area = ' = 60 sq in. Use leader with diameter of 9 in.
•4UU
b. Stack area = 0.7 X 60 = 42 sq in. Use stack %y% in. by 12 in.
60
c. Register gross area — — = 85.7 sq in. Use register 8 in. by 12 in.
3 • The calculated heat loss of a house is 130,000 Btu per hour. Find the grate
area required for the furnace under the following conditions :
Heating value of coal = 12,500 Btu per Ib.
Furnace efficiency = 55 per cent.
Combustion rate — 7.5 Ib per sq ft per hour.
Ratio of heating surface to grate area of furnace = 20 to 1.
Register temperature — 175 F.
Loss between furnace and registers = 20 per cent.
- ^ 1.2 X 144 X 130,000 onn _ .
Gratearea = 0.60 X 12,500 XTS ~ 3"'5 Sq m'
Grate diameter = 22.6 in.
Use grate with diameter of 23 in.
4 • If in Question 3 the conditions were the same except that the ratio of
heating surface to grate area of furnace was 24 to 1, what size grate would be
required for the furnace?
_. 1.2 X 144 X 130,000 .. 1 399.5 Q7n .
Gratearea » 12>500 x 7>5 X x + 0.02 (24 - 20) = T08 = 370 sq m.
Grate diameter = 21.7 sq in.
Select grate with diameter of 22 in.
5 • Name the items involved in the design of a furnace heating system.
a. Heat loss from each room, Btu.
b. Area and dimensions of warm-air pipes in basement, inches.
c. Area and dimensions of vertical pipes, inches.
d. Free and gross area and dimensions of warm-air registers, inches.
e. Area and dimensions of recirculating or outside air ducts, inches.
/. Free and gross area and dimensions of recirculating registers, inches.
g. Size of furnace necessary to supply the warm air to overcome the heat loss.
h. Area and dimension of chimney and smoke pipe, inches.
6 • Discuss the design features of recirculating ducts.
a. Their area should be equal to or greater than that of the supply ducts.
b. They should be streamlined, and have a minimum number of turns.
c. All runs should be as short as possible.
d. Account should be taken of all cold walls and window areas in determining sizes and
positions of return air inlets.
e. The return line should be pitched downward toward the furnace. It should be
designed to minimize friction.
/. The top of the shoe or boot should never be above the grate level.
403
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
7 • Discuss the use of a booster fan. What effect has a booster fan at low
operating temperatures? At high ones?
A booster fan is useful in accelerating the air flow past the surface of a low temperature
furnace, where only a small weight differential in the air is created, and in unbalancing
a gravity system so flow is established. The first use involves the entire plant, and
increases efficiency about 10 per cent with low temperature operation; the second
involves only the leaders in which air flow is accelerated. At high operating ^ tempera-
tures the difference in weight between warm outgoing air and cool incoming air is great
enough to make a booster unnecessary with ordinary gravity systems.
404
Chapter 25
BOILERS
Cast-Iron Boilers, Steel Boilers, Special Heating Boilers, Gas-
Fired Boilers, Hot Water Supply Boilers, Furnace Design, Heating
Surface, Testing and Rating Codes, Output, Efficiency, Selection
of Boilers, Connections and Fittings, Erection, Operation and
Maintenance, Boiler Insulation
STEAM and hot water boilers for low pressure heating work are built in
a wide variety of types, many of which are illustrated in the Catalog
Data Section, and are classified as (1) cast-iron sectional, (2) steel fire
tube, (3) steel water tube, and (4) special.
CAST-IRON BOILERS
Cast-iron boilers may be of round pattern with circular grate and hori-
zontal pancake sections joined by push nipples and tie rods, or of rec-
tangular pattern with vertical sections. The latter type may be either of
outside header construction where each section is independent of the other
and the water and steam connections are made externally through these
headers, or assembled with push nipples and tie rods, in which case the
water and steam connections are internal.
Cast-iron boilers usually are shipped knocked down to facilitate hand-
ling at the place of installation where assembly is made. One of the chief
advantages of cast-iron boilers is that the separate sections can be taken
into or out of basements and other places more or less inaccessible after
the building is constructed. This feature is of importance in making
repairs to or replacing a damaged or worn out boiler and should be given
consideration in the original selection. Sufficient space should be pro-
vided in the boiler room for assembling the boiler and for disassembling it
conveniently if repairs are needed. With the outside header type of boiler
a damaged section in the middle of the boiler can be removed without
disturbing the other sections and sufficient side clearance should be
provided for this contingency.
Capacities of cast-iron boilers range from that required for small
residences up to about 18,000 sq ft of steam radiation. For larger loads,
cast-iron boilers must be installed in multiple, or a steel boiler must be
used. In most cases cast-iron boilers are limited to working pressures of
15 Ib for steam and 30 Ib for water. Special types are built for hot water
supply which will withstand higher local water pressures.
STEEL BOILERS
Two general classifications may be applied to steel boilers: first, with
regard to the relative position of water and hot gases, distinguished as fire
405
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
tube or water tube; second, with regard to arrangement of furnace and
flues, as (1) horizontal return tubular (HRT) boilers, (2) portable (self-
contained) firebox boilers with either water or fire tubes, and (3) water
tube boilers of the power type.
Fire tube boilers are constructed so that the water available to produce
steam is contained in comparatively large bodies distributed outside of the
boiler tubes, the hot gases passing within the tubes. In water tube boilers,
the water is circulated within the boiler tubes, heat being applied ex-
ternally to them.
The HRT boiler is the oldest type and consists of a horizontal cylin-
drical shell with fire tubes, enclosed in brickwork to form the furnace and
TABLE 1. PRACTICAL COMBUSTION RATES FOR SMALL COAL-FIRED HEATING BOILERS
OPERATING ON NATURAL DRAFT OF FROM J4 IN. TO y% IN. WATER*
KIND OP COAL
SQ FT GRATE
LB OP COAL PER SQ FT
GRATE PER HOUR
No. 1 Buckwheat Anthracite
Up to 4
5 to 9
10 to 14
15 to 19
20 to 25
3
3H
4
4H
5
Anthracite Pea
Up to 9
10 to 19
20 to 25
5
5H
6
Anthracite Nut and Larger
Up to 4
5 to 9
10 to 14
15 to 19
20 to 25
8
9
10
11
13
Bituminous
Up to 4
5 to 14
15 and above
9.5
12
15.5
aSteel boilers usually have higher combustion rates for grate areas exceeding 15 sq ft than those indicated
in this table.
combustion chamber. All heating surfaces and the interior of the boiler
are accessible for both cleaning and inspection. Horizontal return tubular
boilers, especially the larger sizes, should be suspended from structural
columns and beams independent of the brick setting. Small HRT boilers
sometimes are supported by brackets resting on the brick setting.
Portable firebox boilers are the more generally used type of steel heating
boilers, their outstanding characteristic being the water- jacketed firebo?c
which eliminates virtually all brickwork. They are shipped in one piece
from the factory and come to the job ready for immediate hook-up to
piping. They may be of welded or riveted construction and have either
water or fire tubes. Manufacturers' catalogs usually list heating surface
as well as grate area. The elimination of brickwork also makes this type
the most compact of steel boilers as well as the lowest in first cost.
Water tube boilers. For large heating loads water tube boilers are quite
frequently used. They usually require more head room than other types
of boilers but require considerably less floor space and make possible a
406
CHAPTER 25 — BOILERS
much higher rate of evaporation per square foot of heating surface, with
proper setting, baffling and draft. Water tube boilers used for heating
purposes are brick set, supported on structural steel columns and have the
brick setting encased in an insulated steel housing to prevent air infiltra-
tion and to minimize heat losses. For large heating loads at a high rate of
evaporation, such boilers should be operated at pressures above 15 Ib per
square inch with a pressure-reducing valve on the connection to the
heating main.
SPECIAL HEATING BOILERS
A special type of boiler, known as the magazine feed boiler, has been
developed for the burning of small sizes of anthracite. These are built of
both cast-iron and steel, and have a large fuel carrying capacity which
results in longer firing periods than would be the case with the standard
types using buckwheat sizes of coal. Special attention must be given to
insure adequate draft and proper chimney sizes and connections.
Oil-burner boiler units, in which a special boiler has been designed with
a furnace shaped to suit the particular burner used, have been developed
by a number of manufacturers. These usually are compact units with the
burner and all controls enclosed within an insulated steel jacket. Ample
furnace volume is provided for efficient combustion, and the heating
surfaces are proportioned for effective heat transfer. Consequently,
higher efficiencies are obtainable than with the ordinary coal fired boiler
converted to oil firing.
GAS-FIRED BOILERS
Gas boilers have assumed a well-defined individuality. The usual boiler
is sectional in construction with a number of independent burners placed
beneath the sections. In most boilers each section has its own burner. In
all cases the sections are placed quite closely together, much closer than
would be possible when burning a soot-forming fuel. The effort of the
designer is always to break the hot gas up into thin streams, so that all
particles of the heat-carrying gases can come as close as possible to the
heat-absorbing surfaces. Because there is no fuel bed resistance and because
the gas company supplies the motive power to draw in the air necessary
for combustion (in the form of the initial gas pressure), draft losses through
gas boilers are low.
HOT WATER SUPPLY BOILERS
Boilers for hot water supply are classified as direct, if the water heated
passes through the boiler, and as indirect, if the water heated does not
come in contact with the water or steam in the boiler.
Direct heaters are built to operate at the pressures found in city supply
mains and are tested at pressures from 200 to 300 Ib per square inch.
The life of direct heaters depends almost entirely on the scale-making
properties of the water supplied. If water temperatures are maintained
below 140 F the life of the heater will be much longer than if higher
temperatures are used, owing to decreased scale formation and minimized
corrosion below 140 F. Direct water heaters in some cases are designed
to burn refuse and garbage.
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Indirect heaters generally consist of steam boilers in connection with
heat exchangers of the coil or tube types which transmit the heat from the
steam to the water. This type of installation has the following advantages :
1. The boiler operates at low pressure.
2. The boiler is protected from scale and corrosion,
3. The scale is formed in the heat exchanger in which the parts to which the scale
is attached can be cleaned or replaced. The accumulation of scale does not affect
efficiency although it will affect the capacity of the heat exchanger.
4. Discoloration of water may be prevented if the water supply comes in contact
with only non-ferrous metal.
Where a steam heating system is installed, the domestic hot water
usually is obtained from an indirect heater placed below the water line of
the boiler.
FURNACE DESIGN
Good efficiency and proper boiler performance are dependent on cor-
rect furnace design embodying sufficient volume for burning the par-
ticular fuel at hand, which requires thorough mixing of air and gases at
a high temperature with a velocity low enough to permit complete com-
bustion of all the volatiles. On account of the small amount of volatiles
contained in coke, anthracite, and semi-bituminous coal, these fuels can
be burned efficiently with less furnace volume than is required for bi-
tuminous coal, the combustion space being proportioned according to the
amount of volatiles present.
Combustion should take place before the gases are cooled by the boiler
heating surface, and the volume of the furnace must be sufficient for this
purpose. The furnace temperature must be maintained sufficiently high
to produce complete combustion, thus resulting in a higher CO 2 content
and the absence of CO. Hydrocarbon gases ignite at temperatures
varying from 1000 to 1500 F.
The question of furnace proportions, particularly in regard to mechani-
cal stoker installations, has been given some consideration by various
manufacturers' associations. Arbitrary values have been recommended
for minimum dimensions. A customary rule-of-thumb method of figuring
furnace volumes is to allow 1 cu ft of space for a maximum heat release
of 50,000 Btu per hour. This value is equivalent to allowing approxi-
mately 1 cu ft for each developed horsepower, and it is approved by
most smoke prevention organizations.
The setting height will vary with the type of stoker. In an overfeed
stoker, for instance, all the volatiles must be burned in the combustion
chamber and, therefore, a greater distance should be allowed than for an
underfeed stoker where a considerable portion of the gas is burned while
passing through the incandescent fuel bed. The design of the boiler also
may affect the setting height, since in certain types the gas enters the
tubes immediately after leaving the combustion chamber, while in others
it passes over a bridge wall and toward the rear, thus giving a better
opportunity for combustion by obtaining a longer travel before entering
the tubes.
To secure suitable furnace volume, especially for mechanical stokers or
oil burners, it often is necessary either to pit the stoker or oil burner, or
408
CHAPTER 25 — BOILERS
where water line conditions and headroom permit, to raise the boiler on a
brick foundation setting.
Smokeless combustion of the more volatile bituminous coals is furthered
by the use of mechanical stokers. (See Chapter 28.) Smokeless com-
bustion in hand-fired boilers burning high volatile solid fuel is aided (1)
by the use of double grates with down-draft through the upper grate, (2)
by the use of a curtain section through which preheated auxiliary air is
introduced over the fire toward the rear of the boiler, and (3) by the intro-
duction of preheated air through passages at the front of the boiler. All
three methods depend largely on mixing secondary air with the partially
burned volatiles and causing this mixture to pass over an incandescent
fuel bed, thus tending to secure more complete combustion than is pos-
sible in boilers without such provision.
HEATING SURFACE
Boiler heating surface is that portion of the surface of the heat transfer
apparatus in contact with the fluid being heated on one side and the gas or
refractory being cooled on the other side. Heating surface on which the
fire shines is known as direct or radiant surface and that in contact with
hot gases only, as indirect or convection surface. The amount of heating
surface, its distribution and the temperatures on either side thereof
influence the capacity of any boiler.
Direct heating surface is more valuable than indirect per square foot
because it is subjected to a higher temperature and also, in the case of
solid fuel, because it is in position to receive the full radiant energy of the
fuel bed. The heat transfer capacity of a radiant heating surface may be
as high as 6 to 8 times that of an indirect surface. This is one of the
reasons why the water legs of some boilers have been extended, especially
in the case of stoker firing where the extra amount of combustion chamber
secured by an extension of the water legs is important. For the same
reason, care should be exercised in building a refractory combustion
chamber in an oil-burning boiler so as not to screen any more of this
valuable surface with refractories than is necessary for good combustion.
The effectiveness of the heating surface depends on its cleanliness, its
location in the boiler, and the shape of the gas passages. Investigations1
by the U. S. Bureau of Mines show that:
1. A boiler in which the heating surface is arranged to give long gas passages of small
cross-section will be more efficient than a boiler in which the gas passages are short and of
larger cross-section.
2. The efficiency of a water tube boiler increases as the free area between individual
tubes decreases and as the length of the gas pass increases.
3. By inserting baffles so that the heating surface is arranged in series with respect to
the gas flow, the boiler efficiency will be increased.
The area of the gas passages must not be so small as to cause excessive
resistance to the flow of gases where natural draft is employed.
Heat Transfer Rates
Practical rates of heat transfer in heating boilers will average about
!See U. S. Bureau of Mines Bulletin No. IS, The Transmission of Heat into Steam Boilers.
409
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
3300 Btu per sq ft per hour for hand-fired boilers and 4000 Btu per sq ft
per hour for mechanically fired boilers when operating at design load2.
When operating at maximum load2 these values will run between 5000 and
6000 Btu per sq ft per hour. Boilers operating under favorable conditions
at the above heat transfer rates will give exit gas temperatures that are
considered consistent with good practice.
TESTING AND RATING CODES
The Society has adopted three solid fuel testing codes, a solid fuel
rating code and an oil fuel testing code. A.S.H.V.E. Standard and Short
Form Heat Balance Codes for Testing Low-Pressure Steam Heating
Solid Fuel Boilers— Codes 1 and 2 — (Revision of June 1929)3, are intended
to provide a method for conducting and reporting tests to determine heat
efficiency and performance characteristics. A.S.H.V.E. Performance
Test Code for Steam Heating Solid Fuel Boilers — Code No. 3 — (Edition of
1929)3 is intended for use with A.S.H.V.E. Code for Rating Steam Heating
Solid Fuel Hand-Fired Boilers4. The object of this test code is to specify
the tests to be conducted and to provide a method for conducting and
reporting tests to determine the efficiencies and performance of the boiler.
The A.S.H.V.E. Standard Code for Testing Steam Heating Boilers
Burning Oil Fuel5 is intended to provide a standard method for con-
ducting and reporting tests to determine the heating efficiency and per-
formance characteristics when oil fuel is used with steam heating boilers.
The Steel Heating Boiler Institute suggests a single number dimensional
rating in the S.H.B.I. Code for the Rating of Low-Pressure Heating
Boilers by Their Physical Characteristics6.
BOILER OUTPUT
Boiler output as defined in A.S.H.V.E. Performance Test Code for
Steam Heating Solid Fuel Boilers (Code No. 3) is the quantity of heat
available at the boiler nozzle with the boiler normally insulated. It
should be based on actual tests conducted in accordance with this code.
This output is usually stated in Btu and in square feet of equivalent heat-
ing surface (radiation). According to the A.S.H.V.E. Standard Code for
Rating Steam Heating Solid Fuel Hand-Fired Boilers, the performance
data should be given in tabular or curve form on the following items for at
least five outputs ranging from maximum down to 35 per cent of maxi-
mum: (1) fuel available, (2) combustion rate, (3) efficiency, (4) draft
tension, (5) flue gas temperature. The only definite restriction placed on
setting the maximum output is that priming shall not exceed 2 per cent.
These curves provide complete data regarding the performance of the
boiler under test conditions. Certain other pertinent information, such as
grate area, heating surface and chimney dimensions is desirable also in
forming an opinion of how the boiler will perform in actual service.
The output of large heating boilers is frequently stated in terms of
•For definitions of design load and maximum load see pages 411 and 412.
•See A.S.H.V.E. TRANSACTIONS, Vol. 35, 1929. Also Chapter 41,
<See A.S.H.V.E. TRANSACTIONS, Vol. 36, 1930. Also Chapter 41.
*See A.S.H.V.E. TRANSACTIONS, Vol. 37, 1931. Also Chapter 41.
•See Rating of Heating Boilers by Their Physical Characteristics, by C. E. Branson (A.S.H.V.E. TRANS-
ACTIONS, Vol. 36, 1930).
410
CHAPTER 25 — BOILERS
boiler horsepower instead of in Btu per hour or square feet of equivalent
radiation.
Boiler Horsepower: The evaporation of 34.5 Ib of water per hour
from and at 212 F which is equivalent to a heat output of 970.2 X 34.5 =
33,471.9 Btu per hour.
Equivalent Evaporation: The amount of water a boiler would
evaporate, in pounds per hour, if it received feed water at 212 F and
vaporized it at this same temperature and at atmospheric pressure.
It is usually considered that 10 sq ft of boiler heating surface will pro-
duce a rated boiler horsepower. A rated boiler horsepower in turn
can carry a design load of from 100 to 140 sq ft of equivalent radiation.
It is apparent, therefore, that 1 sq ft of boiler heating surface can carry a
design load of from 10 to 14 sq ft of equivalent radiation, or somewhat
more if the boiler is forced above rating. The application of these values
is discussed under the heading Selection of Boilers.
BOILER EFFICIENCY
The term efficiency as used for guarantees of boiler performance is
usually construed as follows:
1. Solid Fuels. The efficiency of the boiler alone is the ratio of the heat absorbed by
the water and steam in the boiler per pound of combustible burned on the grate to the
calorific value of 1 Ib of combustible as fired. The combined, efficiency of 'boiler, furnace
and grate is the ratio of the heat absorbed by the water and steam in the boiler per pound
of fuel as fired to the calorific value of 1 Ib of fuel as fired.
2. Liquid Fuels. The combined efficiency of. boiler, furnace and burner is the ratio of
the heat absorbed by the water and steam in the boiler per pound of fuel to the calorific
value of 1 Ib of fuel.
Solid fuel boilers usually show an efficiency of 50 to 75 per cent when
operated under favorable conditions at their rated capacities. Infor-
mation on the combined efficiencies of boiler, furnace and burner has
resulted from research conducted at Yale University in cooperation with
the A.S.H.V.E. Research Laboratory and the American Oil Burner
Association1. For general information on heating efficiencies see Chapter
29.
SELECTION OF BOILERS
Estimated Design Load: The load, stated in Btu per hour or equiv-
alent direct radiation, as estimated by the purchaser for the conditions of
inside and outside temperature for which the amount of installed radiation
was determined is the sum of the heat emission of the radiation to, be
actually installed plus the allowance for the heat loss of the connecting
piping plus the heat requirement for any apparatus requiring heat con-
nected with the system (A.S.H.V.E. Standard Code for Rating Steam
Heating Solid Fuel Hand-Fired Boilers— Edition of April, 1932).
The estimated design load is the sum of the following three items8:
1. The estimated heat emission in Btu per hour of the connected radiation (direct,
indirect or central fan) to be installed.
'See A.S.H.V.E. research papers entitled Study of the Characteristics of Oil Burners and Heating
Boilers, by L. E. Seeley and E. J. Tavanlar (A.S.H.V.E. TRANSACTIONS, Vol. 37, 1931), and A Study of
Intermittent Operation of Oil Burners, by L. E. Seeley and J. H. Powers (A.S.H.V.E. TRANSACTIONS,
Vol. 38, 1932).
•See A.S.H.V.E. Code of Minimum Requirements for the Heating and Ventilation of Buildings (Edition
of 1929).
411
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
2. The estimated maximum heat in Btu per hour required to supply water heaters
or other apparatus to be connected to the boiler.
3. The estimated heat emission in Btu per hour of the piping connecting the radiation
and other apparatus to the boiler.
Estimated Maximum Load: Construed to mean the load stated in
Btu per hour or the equivalent direct radiation that has been estimated by
the purchaser to be the greatest or maximum load that the boiler will be
called upon to carry. (A.S.H.V.E. Standard Code for Rating Steam
Heating Solid Fuel Hand-Fired Boilers— Edition of April, 1932.)
The estimated maximum load is given by8:
4. The estimated increase in the normal load in Btu per hour due to starting up cold
radiation. This percentage of increase is to be based on the sum of Items 1, 2 and 3
and the heating-up factors given in Table 2.
TABLE 2. WARMING-UP ALLOWANCES FOR Low PRESSURE STEAM AND
HOT WATER HEATING BOILERSSI t>, c
DESIGN LOAD (REPRESENTING SUMMATION OF ITEMS 1, 2, AND 3,d
PERCENTAGE CAPACITT TO ADD
FOR WARMING UP
Btu per Hour
Equivalent Square Feet of Radiationd
. Up to 100,000
100,000 to 200,000
200,000 to 600,000
600,000 to 1,200,000
1,200,000 to 1,800,000
Above 1,800,000
Up to 420
420 to 840
840 to 2500
2500 to 5000
5000 to 7500
Above 7500
65
60
55
50
45
40
aThis table is taken from the A.S.H.V.E. Code of Minimum Requirements for the Heating and Venti-
lation of Buildings, except that the second column 'has been added for convenience in interpreting the design
load in terms of equivalent square feet of radiation.
bSee also Time Analysis in Starting Heating Apparatus, by Ralph C. Taggert (A.S.H.V.E. TRANSAC-
TIONS, Vol. 19, 1913); Report of A.S.H.V.E. Continuing Committee on Codes for Testing and Rating Steam
Heating Solid Fuel Boilers (A.S.H.V.E. TRANSACTIONS, yol. 36, 1930); Selecting the Right Size Heating
Boiler, by Sabin Crocker (Heating, Piping and Air Conditioning, March, 1932).
cThis table refers to hand-fired solid fuel boilers. A factor of 25 per cent over design load is adequate
when oil or gas are used as fuels.
d240 Btu per square foot.
Other things to be considered are:
5. Efficiency with hard or soft coal, gas, or oil firing, as the case may be.
6. Grate area with hand-fired coal, or fuel burning rate with stokers, oil, or gas.
7. Combustion space in the furnace.
8. Type of heat liberation, whether continuous or intermittent, or a combination of
both.
9. Miscellaneous items consisting of draft available, character of attendance, pos-
sibility of future extension, possibility of breakdown, headroom in the boiler room.
Radiation Load
The connected radiation (Item 1) is determined by calculating the heat
losses in accordance with data given in Chapters 5, 6 and 7, and dividing
by 240 to change to square feet of equivalent radiation as explained in
Chapter 30. For hot water, the emission commonly used is 150 Btu per
square foot, but the actual emission depends on the temperature of the
medium in the heating units and of the surrounding air. (See Chapter 30.)
Although it is customary to use the actual connected load in equivalent
square feet of radiation for selecting the size of boiler, this connected load
usually represents a reserve in heating capacity to provide for infiltration
in the various spaces of the building to be heated, which reserve, however,
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CHAPTER 25 — BOILERS
is not in use at all places at the same time, or in any one place at all times.
For a further discussion of this subject see Chapter 6.
Hot Water Supply Load
When the hot water supply (Item 2) is heated by the building heating
boiler, this load must be taken into consideration in sizing the boiler. The
§u.
0 w
iboo 2000 3000 4000 5000 eooo 7000 u
OUTPUT, SQ. FT. EQUIVALENT STEAM RADIATION (240 BTU PER SQ.FT.)
BOILER DATA— GRATE ARE A,SQ. FT. 18-0 FUEL— BITUMINOUS 3/4" LUMP
HEATING SURFACE.SQ. FT. 254 ANALYSES- VOLATILE MATTER 34-06%
WEIGHT, LB.
FUEL CAPACITY, LB.
FUEL AVAILABLE, LB.
FUEL DEPTH, IN
9160
651
414.
10
FIXED CARBON
ASH
SULPHUR
MOISTURE
BTU PERLB.
55.44
0.67
2.66
3.00
13,655
FIG. 1. TYPICAL PERFORMANCE CURVES FOR A 36-iN. CAST-IRON SECTIONAL STEAM
HEATING BOILER, BASED ON THE A.S.H.V.E. CODE FOR RATING STEAM
HEATING SOLID FUEL HAND-FIRED BOILERS
allowance to be made will depend on the amount of water heated and its
temperature rise. A good approximation is to add 4 sq ft of equivalent
radiation for each gallon of water heated per hour through a temperature
range of 100 F. For more specific information, see Chapter 35.
Piping Tax (Item 3)
It is common practice to add a flat percentage allowance to the
equivalent connected radiation to provide for the heat loss from bare and
covered pipe in the supply and return lines. The use of a flat allowance of
25 per cent for steam systems and 35 per cent for hot water systems is
preferable to ignoring entirely the load due to heat loss from the supply
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
and return lines, but better practice, especially when there is much bare
pipe, is to compute the emission from both bare and covered pipe surface
in accordance with data in Chapter 36. With direct radiation served by
bare supply and return piping the percentages may be higher than those
stated, while in the case of unit heaters where the output is concentrated
in a few locations, the piping tax may be 10 per cent or less.
Warming-up Allowance
The warming-up allowance represents the load due to heating the boiler
and contents to operating temperature and heating up cold radiation and
piping. (See Item 4.) The factors to be used for determining the
allowance to be made should be selected from Table 2 and should be
applied to the estimated design load as determined by Items 1, 2 and 3.
Performance Curves for Boiler Selection
In the selection of a boiler to meet the estimated load, the A.S.H.V.E.
Standard Code for Rating Steam Heating Solid Fuel Hand-Fired Boilers
recommends the use of performance curves based on actual tests con-
ducted in accordance with the A.S.H.V.E. Performance Test Code for
Steam Heating Solid Fuel Boilers (Code No. 3), similar to the typical
curves shown in Fig. 1. It should be understood that performance data
apply to test conditions and that a reasonable allowance should be made
for decreased output resulting from soot deposit, poor fuel or inefficient
attention.
Selection Based on Heating Surface and Grate Area
Where performance curves are not available, a good general rule for
conventionally-designed boilers is to provide 1 sq ft of boiler heating
surface for each 14 sq ft of equivalent radiation (240 Btu per square foot)
represented by the design load consisting of connected radiation, piping
tax and domestic water heating load. As stated in the section on Boiler
Output, this is equivalent to allowing 10 sq ft of boiler heating surface per
boiler horsepower. In this case it is assumed that the maximum load
including the warming-up allowance will be provided for by operating the
boiler in excess of the design load, that is, in excess of the 100 per cent
rating on a boiler-horsepower basis.
Due to the wide variation encountered in manufacturers' ratings for
boilers of approximately the same capacity, it is advisable to check the
grate area required for heating boilers burning solid fuel by means of the
following formula:
G = ~CX FXE (1)
where
G =a grate area, square feet.
H ~ required total heat output of the boiler, Btu per hour (see Selection of Boilers,
p. 411),
C = combustion rate in pounds of dry coal per square foot of grate area per hour,
depending on the kind of fuel and size of boiler as given in Table 1.
F = calorific value of fuel, Btu per pound.
E s= efficiency of boiler, usually taken as 0.60.
Example 1. Determine the grate area for a required heat output of the boiler of
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CHAPTER 25 — BOILERS
500,000 Btu per hour, a combustion rate of 6 Ib per hour, a calorific value of 13,000 JBtu
per pound, and an efficiency of 60 per cent.
r _ 500,000 ' 1A« r
G " ex 13,000x0.60 " 10-7 sq ft ; ".,;;.;
The boiler selected should have a grate area not less than that deter-
mined by Formula 1. With small boilers where it is desired to- provide
sufficient coal capacity for approximately an eight-hour firing period plus
a 20 per cent reserve for igniting a new charge, more grate area may be
required depending upon the depth of the fuel pot.
Selection of Gas-Fired Boilers
Gas-heating appliances should be selected in accordance with factors
given in Table 1, Chapter 28, which include an allowance for heating up
cold radiation, and for the piping tax. These factors are for thermo--
statically-controlled systems; in case manual operation is desired, a
warming-up allowance of 100 per cent is recommended by the A^G'.A:
A gas boiler selected by the use of the A .G.A. factors will be the minimum
size boiler which can carry the load. From a fuel economy standpoint, it
may be advisable to select a somewhat larger boiler and then throttle the
gas and air adjustments as required. "This will tend to' give a low stack
temperature with high efficiency and at the same time provide reserve
capacity in case the load is underestimated or more is added in the future:
Conversions
In the case of a solid fuel boiler converted to gas burning, the heat units
supplied in the gas should be approximately twice the 'connected heating
load. A combustion efficiency of 75 per cent for a conversion" installation
would provide a boiler output of 2 X 0.75 = 1.5 times the connected Io4d-,
which allows 50 per cent for piping tax and pick-up. . The presumption for
a conversion" job is that the boiler already is installed and probably will
not be made larger; therefore, it is a matter of setting a gas-burning rate
to obtain best results with the available surface. The conversion of a coal
or oil boiler to gas burning is accomplished much more rapidly than the
reverse since but little furnace volume need be provided for the proper
combustion of gas.
Other Considerations in Selection of Boilers
As it will usually be found that several boilers will meet the speci-
fications, the final selection of the boiler may be influenced by other con-
siderations, some of which are :
1. Dimensions of boiler. . . .
2. Durability under service.
3. Convenience in 'firing and cleaning. ' . ' " - * - - -
4. Adaptability to changes in fuel and kind of attention.
5. Height of water line. . : \ ' , . ' . ' ' '
In large installations, the use of several smaller boiler units instead of
one larger one will obtain greater flexibility and economy by, permitting
the operation, at the best efficiency, of the required number of units
according to the heat requirements. • - • _
Boiler rooms should, if possible, be situated at a central point with
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
respect to the building and should be designed for a maximum of natural
light. The space in front of the boilers should be sufficient for firing,
stoking, ash removal and cleaning or renewal of flues, and should be at
least 3 ft greater than the length of the boiler firebox.
A space of at least 3 ft should be allowed on at least one side of every
boiler for convenience of erection and for accessibility to the various
dampers, cleanouts and trimmings. The space at the rear of the boiler
should be ample for the chimney connection and for cleanouts, and with
large boilers the rear clearance should be at least 3 ft in width.
The boiler room height should be sufficient for the location of boiler
accessories and for proper installation of piping. In general the ceiling
height for small steam boilers should be at least 3 ft above the normal
boiler water line. With vapor heating, especially, the height above the
boiler water line is of vital importance.
When steel boilers are used, space should be provided for the removal
and replacement of tubes.
CONNECTIONS AND FITTINGS
The velocity of flow through the outlets of low pressure steam heating
boilers should not exceed 15 to 25 fps if fluctuation of the water line and
undue en trainmen t of moisture are to be avoided. Steam or water outlet
connections preferably should be the full size of the manufacturers'
tapping and should extend vertically to the maximum height available
above the boiler. For gravity circulating steam heating systems, it is
recommended that a Hartford Loop, described in Chapter 32, be utilized
in making the return connection.
Particular attention should be given to fitting connections to secure con-
formity with the A.S.M.E. Boiler Construction Code for Low Pressure
Heating Boilers. Attention is called in particular to pressure gage piping,
water gage connections and safety valve capacity.
Steam gages should be fitted with a water seal and a shut-off consisting
of a cock with either a tee or lever handle which is parallel to the pipe
when the cock is open. Steam 'gage connections should be of copper or
brass when smaller than 1 in. J.P.5.9 if the gage is more than 5 ft from the
boiler connection, and also in any case where the connection is less than
% in. I.P.S.
Each steam or vapor boiler should have at least one water gage glass and
two or more gage cocks located within the range of the visible length of the
glass. The water gage fittings or gage cocks may be direct connected to
the boiler, if so located by the manufacturer, or may be mounted on a
separate water column. No connections, except for combustion regu-
lators, drains or steam gages, should be placed on the pipes connecting
the water column and the boiler. If the water column or gage glass is con-
nected to the boiler by pipe and fittings, a cross, tee or equivalent, in which
a cleanout plug or a drain valve and piping may be attached, should be
placed in the water connection at every right-angle turn to facilitate
cleaning. The water line in steam boilers should be carried at the level
specified by the boiler manufacturer.
. Code, Identification of Piping Systems.
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CHAPTER 25 — BOILERS
Safety valves should be capable of discharging all the steam that can be
generated by the boiler without allowing the pressure to rise more than
5 Ib above the maximum allowable working pressure of the boiler. This
should be borne in mind particularly in the case of boilers equipped with
mechanical stokers or oil burners where the amount of grate area has
little significance as to the steam generating capacity of the boiler.
Where a return header is used on a cast-iron sectional boiler to distribute
the returns to both rear tappings, it is advisable to provide full size
plugged tees instead of elbows where the branch connections enter the
return tappings. This facilitates cleaning sludge from the bottom of the
boiler sections through the large plugged openings. An equivalent clean-
out plug should be provided in the case of a single return connection.
Blow-off or drain connections should be made near the boiler and so
arranged that the entire system may be drained of water by opening the
drain cock. In the case of two or more boilers separate blow-off connec-
tions must be provided for each boiler on the boiler side of the stop valve
on the main return connection.
Water service connections must be provided for both steam and water
boilers, for refilling and for the addition of make-up water to boilers. This
connection is usually of galvanized steel pipe, and is made to the return
main near the boiler or boilers.
For further data on pipe connections for steam and hot water heating
systems, see Chapters 32 and 33 and the A.S.M.E. Boiler Construction
Code for Low Pressure Heating Boilers.
Smoke Breeching and Chimney Connections. The breeching or smoke
pipe from the boiler outlet to the chimney should be air-tight and as short
and direct as possible, preference being given to long radius and 45-deg
instead of 90-deg bends. The breeching entering a brick chimney should
not project beyond the flue lining and where practicable it should be
grouted up from the inside of the chimney. A thimble or sleeve grout
usually is provided where the breeching enters a brick chimney.
Where a battery of boilers is connected into a breeching each boiler
should be provided with a tight damper. The breeching for a battery
of boilers should not be reduced in size as it goes to the more remote
boilers. Good connections made to a good chimney will usually result in
a rapid response by the boilers to demands for heat.
ERECTION, OPERATION, AND MAINTENANCE
The directions of the boiler manufacturer always should be read before
the assembly or installation of any boiler is started, even though the
contractor may be familiar with the boiler. All joints requiring boiler
putty or cement which cannot be reached after assembly is complete
must be finished as the assembly progresses.
The following precautions should be taken in all installations to prevent
damage to the boiler:
1. There should be provided proper and convenient drainage connections for use if
the boiler is not in operation during freezing weather.
2. Strains on the boiler due to movement of piping during expansion should be
prevented by suitable anchoring of piping and by proper provision for pipe expansion
and contraction.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
3. Direct impingement of too intense local heat upon any part of the boiler surface,
as with .oil burners, should be avoided by protecting the surface with firebrick or other
refractory material. -
4. Condensation must flow back to the boiler as rapidly and uniformly as possible.
Return connections should prevent the water from backing out of the boiler.
5. Automatic boiler feeders and low water cut-off devices which shut off the source
of heat if the water in the boiler falls below a safe level are recommended for boilers
mechanically fired.
Boiler Troubles
A complaint regarding boiler operation generally will be found to be
due to one of the following:
- 1. The boiler fails to deliver enough heat. The cause of this condition may be: (a) poor
draft -r (b) poor fuel; (c} inferior attention or firing; (d) boiler too small; (e) improper
piping; (/) improper arrangement of sections; (g) heating surfaces covered with soot;
and (h) insufficient radiation installed.
2. The water line is unsteady. The cause of this condition may be : (a) grease and dirt
in boiler; (&) water column connected to a very active section and, therefore, not
showing actual water level in boiler; (c) boiler operating at excessive output.
. 3. Water disappears from gage glass. This may be caused by: (a) priming due to
grease and dirt in boiler; (&) too great pressure difference between supply and return
piping preventing return of condensation; (c) valve closed in return line; (d) connection
of bottom of water column into a very active section or thin waterway; (e) improper
connections between boilers in battery permitting boiler with excess pressure to push
returning condensation into boiler with lower pressure.
- 4, Water is^carried over into steam main. This may be caused by: (a) grease and dirt
in boiler; (&) insufficient steam dome or too small steam liberating area; (c) outlet con-
nections of too small area; (d) excessive rate of output; (e) water level carried higher
than specified.
5. Boiler is slow in response to operation of dampers. This may be due to : (a) poor
draft due to air leaks into chimney or breeching; (b) inferior fuel; (c) inferior attention;
(d) accumulation of clinker on grate; (e) boiler too small for the load.
- 6. Boiler requires too frequent cleaning of flues. This may be due to: (a) poor draft;
(b) smoky combustion; (c) too low a rate of combustion; (d) too much excess air in
firebox causing chilling of gases.
1. Boiler smokes through fire door. This may be due to: (a) defective draft in chimney
or incorrect setting of dampers; (b) air leaks into boiler or breeching; (c) gas outlet from
firebox plugged with fuel; (d) dirty or clogged flues; (e} improper reduction in breeching
size.
Cleaning Steam Boilers
All boilers are provided with flue clean-out openings through which the
heating surface can be reached by means of brushes or scrapers. Flues
of solid fuel boilers should be cleaned often to keep the surfaces free of
soot or ash. Gas boiler flues and burners should be cleaned at least once
a year. Oil burning boiler flues should be examined periodically to deter-
mine when cleaning is necessary.
The grease used to lubricate the cutting tools during erection of new
piping systems serves as a carrier for sand and dirt, with the result that
a scum of fine particles and grease accumulates on the surface of the
water in -all new boilers, while heavier particles may settle to the bottom
of the boiler and form sludge. These impurities have a tendency to cause
foaming, preventing the generation of steam and causing an unsteady
water line.
This unavoidable accumulation of oil and grease should be removed
by blowing off the boiler as follows: If not already provided, install a
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CHAPTER 25 — BOILERS
surface blow connection of at least 1J^ in. nominal pipe size with outlet
extended to within 18 in. of the floor or to sewer, inserting a valve in line
close to boiler. Bring the water line to center of outlet, raise steam pres-
sure and while fire is burning briskly open valve in blow-off line. When;
pressure recedes close valve and repeat process adding water at intervals
to maintain proper level. As a final operation bring the pressure in the
boiler to about 10 Ib, close blow-off, draw the fire or stop burner, and open
drain valve. After boiler has cooled partly, fill and flush out several times
before filling it to proper water level for normal service. The use of acids,
alkalis and salts for cleaning is not favored by boiler manufacturers
because of the difficulty of complete removal and the possibility of sub-,
sequent injury.
Insoluble compounds have been developed which are effective, but
special instructions on the proper cleaning compound and directions for
its use in a boiler, as given by the boiler manufacturer, should be carefully
followed.
When soda ash solution is to be used the procedure is to add about 5 Ib
of soda ash for each 1000 sq ft of connected radiation. Fill the boiler with
water until it just overflows from the surface blow outlet pipe and then
fire sufficiently to raise the water temperature to the boiling point without
getting up steam pressure. Crack the boiler feed valve so that a steady
trickle will run out of the overflow pipe. Allow the boiler to simmer from
2 to 4 hours. At the end of this time the grease and sediment should have
passed off through the overflow pipe or loosened sufficiently to drain off
through the bottom blow. Extinguish the fire — preferably by letting it
burn out and then dumping any live coals into the ashpit where water can
be applied with a hose — and open the bottom blow wide. Rinse with
fresh water and refill to the normal water level. If the water in the gage
glass then does not show clear, repeat the process using a stronger soda
ash solution and boiling for a longer time. It sometimes is necessary to
repeat this process several times to completely rid the boiler of grease.
Failure to thoroughly eliminate grease usually results in an unsteady
water line and danger of damaging the boiler through having the crown-
sheet uncovered.
It is common practice when starting new installations to discharge
heating returns to the sewer during the first week of operation. This
prevents the passage of grease, dirt or other foreign matter into the boiler
and consequently may avoid the necessity of cleaning the boiler. During
the time the returns are being passed to the sewer, the feed valve should
be cracked sufficiently to maintain the proper water level in the boiler.
Care of Idle Heating Boilers
Heating boilers are often seriously damaged during summer months
due chiefly to corrosion resulting from the combination of sulphur from
the fuel with the moisture in the cellar air. At the end of the heating
season the following precautions should be taken :
1. All heating surfaces should be cleaned thoroughly of soot, ash and residue, and the
heating surfaces of steel boilers should be given a coating of lubricating oil on the fire
side.
2. All machined surfaces should be coated with oil or grease.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
3. Connections to the chimney should be cleaned and in case of small boilers the pipe
should be placed in a dry place after cleaning.
4. If there is much moisture in the boiler room, it is desirable to drain the boiler to
prevent atmospheric condensation on the heating surfaces of the boiler when they are
below the dew-point temperature. Due to the hazard of some one inadvertently building
a fire in a dry boiler, however, it is safer to keep the boiler filled with water. A hot water
system usually is left filled to the expansion tank.
5. The grates and ashpit should be cleaned.
6. Clean and repack the gage glass if necessary,
7. Remove any rust or other deposit from exposed surfaces by scraping with a wire
brush or sandpaper. After boiler is thoroughly cleaned, apply a coat of preservative
paint where required to external parts normally painted.
8. Inspect all accessories of the boiler carefully to see that they are in good working
order. In this connection, oil all door hinges, damper bearings and regulator parts.
BOILER INSULATION
Insulation for cast-iron boilers is of two general types: (1) plastic
material or blocks wired on, cemented and covered with canvas or duck;
and (2) blocks, sheets or plastic material covered with a metal jacket
furnished by the boiler manufacturer. Self-contained steel firebox boilers
usually are insulated with blocks, cement and canvas, or rock wool
blankets; HRT boilers are brick set and do not require insulation beyond
that provided in the setting. It is essential that the insulation on a boiler
and adjacent piping be of non-combustible material as even slow-burning
insulation constitutes a dangerous fire hazard in case of low water in
the boiler.
REFERENCES
A.S.H.V.E. Code of Minimum Requirements for the Heating and Ventilation of
Buildings.
A.S.H.V.E. Standard and Short Form Heat Balance Codes for Testing Low-Pressure
Steam Heating Solid Fuel Boilers (Codes 1 and 2).
A.S.H.V.E. Performance Test Code for Steam Heating Solid Fuel Boilers (Code No. 3).
A.S.H.V.E. Standard Code for Rating Steam Heating Solid Fuel Hand-Fired Boilers.
Heating, Ventilating and Air Conditioning, by Harding and Willard, Revised Edition,
1932.
A.S.M.E. Boiler Construction Code for Low Pressure Heating Boilers.
Heating and Piping Contractors National Association Standards (boiler selection
tables).
House-Heating, published by American Gas Association.
Handbook of Oil Burning, published by American Oil Burner Association.
Heating and Ventilation, by Allen and Walker (3rd Edition),
Selecting the Right Size Boiler, by Sab in Crocker (Heating, Piping and Air Con-
ditioning, February, March, April, 1932).
PROBLEMS IN PRACTICE
1 • What is meant by a low pressure heating holler?
A low pressure heating boiler is a boiler designed to be operated at less than 15 Ib steam
pressure or 30 Ib water pressure as measured by a gage attached directly to the boiler.
420
CHAPTER 25 — BOILERS
2 • Name the construction materials that distinguish two types of low pressure
heating hoilers.
a. Cast-iron.
b. Steel.
3 • What is the normal rating range of each type of hoiler?
a. Cast-iron boilers are rated at from 200 to 18,000 sq ft EDR.
b. Steel boilers are rated at from 300 to 50,000 sq ft EDR.
4 • a. What is meant by direct boiler heating surface?
b. What is meant by indirect boiler heating surface?
a. Direct boiler heating surface is that boiler surface upon which the fire shines, namely,
the walls of the firebox and the crown sheet.
b. Indirect boiler heating surface is that boiler surface not exposed to the direct rays of
the fire and over which heated gases pass after they have been in contact with the
direct surface. Indirect surface is generally known as convective surface.
5 • What is the average heat transmission rate in heating boilers in Btu per
sq ft of heating surface per hour?
3500 for coal burning boilers; 4200 for oil burning boilers.
6 • What factors contribute to economical fuel operation in low pressure
boilers burning coal or oil?
a. Proper furnace volume for complete combustion.
b. Arrangement of heating surfaces in series to create a turbulent and scrubbing contact
of gases against the convective surfaces.
c. Rapid internal water circulation which will remove steam bubbles from the water
side of heating surfaces and allow other steam bubbles to be formed. Rapid disen-
gagement of steam bubbles increases the steam generating efficiency of each unit
area of heating surface, and thereby lowers flue gas temperatures.
7 • What equipment is usually directly attached to a low pressure heating
hoiler?
For coal burning steam boilers: water column, water gage, tri-cocks, steam gage, lever
pop safety valve, boiler damper regulator.
For coal burning hot water boilers: damper regulator, altitude gage, thermometer, relief
valve.
For oil burning boilers, the damper regulators are omitted and the following additional
equipment is usually attached: automatic water feeder, low water cutout,, a pressure
control, and a water temperature control These are generally furnished by the oil
burner manufacturer and do not come with the boiler.
I • What general precautions regarding the boiler sho
uire a proposed heating installation will work properly?
should he taken to make
a. Select the right size and type of boiler.
b. Be sure the combustion space is proper for the type of fuel burned.
c. Allow sufficient space around the boiler for cleaning.
d. Secure proper height and area of chimney and connecting breeching.
e. Clean the boiler thoroughly and provide surface blowoff connections and bottom
blowoff connections for periodic cleaning after operation is begun,
/. See that the boiler heating surface is cleaned at regular periods.
g. Check flue gas temperatures and make a flue gas analysis at least once a month .
h. Secure information and advice from boiler manufacturer.
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__ AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
9~* -"Below what temperature ^should the water in direct water heaters he main-
tained to reduce scale formation and corrosion?
140 F.
10 • a. What is the heat equivalent of a boiler horsepower?
b. How many -square feet of heating surface are usually required per
boiler horsepower?
a. 33,471.9 Btu per hour.
b. lOsqft.
11 • What is meant by equivalent evaporation?
The amount of water that a boiler would evaporate per hour, if the feed water were at
212 F and if the steam were evaporated at that temperature; this is usually spoken of as
"from and at 212 F."
12 • What loads must be considered in determining the boiler capacity re-
quired for a given installation?
Radiation load.
Hot water supply load.
Piping tax.
Warming-up allowance.
Load allowance for inefficient firing.
13 • A boiler has 6 sq ft of grate area with a possible depth of fuel bed of 18 in.
The fuel burned is bituminous coal with a heat value of 12,500 Btu per Ib,
The efficiency is assumed to be 50 per cent. How great a maximum load will
this boiler carry if it is to be fired every 8 hours and if 20 per cent of the fuel is
to. be left over to kindle the next charge?
Volume of fuel bed = 6 X 1.5 = 9.0 cu ft.
Available volume = 0.80 X 9.0 = 7.2 cu ft. -
Weight of available fuel = 40 X 7.2 = 288.0 Ib.
288 0
Fuel 'burned per hour = — ~- = 36.0 Ib.
o
Heat released = 36.0 X 12,500 X 0.50 « 225,000 Btu per hour.
: • 225 000
Maximum load — — ^Tj — ^ ^38 equivalent square feet.
14 • What are the usual causes of unsteady water line and priming?
Grease and dirt in boiler.
Overload, .resulting in insufficient steam liberating area.
Small outlet connections.
15 • What type of return connection can be used for gravity steam heating
systems to make 'the use of check valves unnecessary?
The Hartford Loop. (See Chapter 32.)
422
Chapter 26
CHIMNEYS AND DRAFT
CALCULATIONS
Natural Draft, Mechanical Draft, Characteristics of Natural
Draft Chimneys, Determining Chimney Sizes, General Equation,
Chimney Construction, Chimneys for Gas Heating
THE design and construction of a chimney is so important a part
of the heating engineer's work that a general knowledge of draft
characterises and calculations is essential.
Draft, in general, may be defined as the pressure difference between the
atmospheric pressure and that at any part of an installation through
which the gases flow. Since a pressure difference implies a head, draft
is a static force. While no element of motion is inferred, yet motion
in the form of circulation of gases throughout an entire boiler plant
installation is the direct result of draft. This motion is due to the pressure
difference, or unbalanced pressure, which compels the gases to flow. Draft
is often classified into two kinds according to whether it is created
thermally or artificially, viz, (1) natural or thermal draft, and (2) arti-
ficial or mechanical draft.
Natural Draft
Natural draft is the difference in pressure produced by the difference in
weight between the relatively hot gases inside a natural draft chimney and
an equivalent column of the cooler outside air, or atmosphere. Natural
draft, in other words, is an unbalanced pressure produced thermally by a
natural draft chimney as the pressure transformer and a temperature
difference. The intensity of natural draft depends, for the most part,
upon the height of the chimney above the grate bar level and also the
temperature difference between the chimney gases and the atmosphere.
A typical natural draft system consists essentially of a relatively tall
chimney built of steel, brick or reinforced concrete, operating with the
relatively hot gases which have passed through the boilers and accessories
and from which all of the heat has not been extracted. Hot gases are an
essential element in the operation of a natural draft system.
A natural draft chimney performs the two-fold service of assisting in
the creation of draft by aspiration and also of discharging the gases at an
elevation sufficient to prevent them from becoming a nuisance.
Natural draft is quite advantageous in installations where the total loss
of draft due to resistances is relatively low and also in plants which have
practically a constant load and whose boilers are seldom operated above
their normal rating. Natural draft systems have been, and are still being,
employed in the operation of large plants during the periods when the
boilers are operated only up to their normal rating. When the rate of
423
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
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424
CHAPTER 26 — CHIMNEYS AND DRAFT CALCULATIONS
operation is increased above their normal rating, some form of mechanical
draft is employed as an auxiliary to overcome the increased resistances or
draft losses. Natural draft systems are used almost exclusively in the
smaller size plants where the amount of gases generated is relatively small
and it would be expensive to install and operate a mechanical draft
system.
The principal advantages of natural draft systems may be summarized
as follows: (1) simplicity, (2) reliability, (3) freedom from mechanical
parts, (4) low cost of maintenance, (5) relatively long life, (6) relatively
low depreciation, and (7) no power required to operate. The principal
disadvantages are: (1) lack of flexibility, (2) irregularity, (3) affected
by surroundings, and (4) affected by temperature changes.
Mechanical Draft
Artificial draft, or mechanical draft, as it is more commonly called, is a
difference in pressure produced either directly or indirectly by a forced
draft fan, an induced draft fan, or aVenturi chimney as the pressure
transformer. The intensity of mechanical draft is dependent for the most
part upon the size of the fan and the speed at which it is operated. The
element of temperature does not enter into the creation of mechanical
draft and therefore its intensity, unlike natural draft, is independent of the
temperature of the gases and the atmosphere. Mechanical draft includes
the induced and Venturi types of draft systems in which the pressure
difference is the result of a suction and also the forced draft system in
which the pressure difference is the result of a blowing. Mechanical draft
systems tend to produce a vacuum or a plenum, according as the system
used in its production creates a pressure difference below, or above,
atmospheric pressure, respectively. A mechanical draft system may be
used either in conjunction with, or as an adjunct to, a natural draft
system.
CHARACTERISTICS OF CHIMNEYS
In order to analyze the performance of a natural draft chimney, it is
advantageous to compare its general operating characteristics with those
of a centrifugal pump and also a centrifugally-induced draft fan, there
being a close similarity among the three. Figs. 1, 2 and 3 show the
general operating characteristics of a typical centrifugally-induced draft
fan, a typical centrifugal pump, and a typical natural draft chimney,
respectively. The draft-capacity curve of the chimney corresponds to the
head-capacity curve of the pump and also to the dynamic-head capacity of
the fan ; the efficiency curve of the chimney to the efficiency curves of the
pump and fan ; and the gas horsepower curve of the chimney to the brake
horsepower curves of the pump and fan.
When the gases in the chimney are stationary, the draft created is
termed the theoretical draft. When the gases are flowing, the theoretical
intensity is diminished by the draft loss due to friction, the difference
between the two being termed the available draft. The general equation
for the available draft intensity of a natural draft chimney with a circular
section is as follows:
425
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
where
Z?a = available draft, inches of water.
H = height of chimney above grate bars, feet.
Bo = barometric pressure corresponding to altitude, inches of mercury.
W0 = unit weight of a cubic foot of air at 0 F and sea level atmospheric pressure,
pounds per cubic foot.
We = unit weight of a cubic foot of chimney gases at 0 F and sea level atmospheric
pressure, pounds per cubic foot.
To « absolute temperature of atmosphere, degrees Fahrenheit.
TC = absolute temperature of chimney gases, degrees Fahrenheit.
W = amount of gases generated in the combustion chamber of the boiler and passing
through the chimney, pounds per second.
/ ~ coefficient of friction.
L = length of friction duct of the chimney, feet.
D = minimum diameter of chimney, feet.
The first term of the right hand expression of Equation 1 represents
the theoretical draft intensity, and the second term, the loss due to friction.
Example 1 . Determine the available draft of a natural draft chimney 200 ft in height
and 10 ft in diameter operating under the following conditions ^atmospheric tempera-
ture, 62 F ; chimney gas temperature, 500 F ; sea level atmospheric pressure, B0 = 29.92
in. of mercury; atmospheric and chimney gas density, 0.0863 and 0.09, respectively;
coefficient of friction, 0.016; length of friction duct, 200 ft. The chimney discharges
100 Ib of gases per second.
Substituting these values in Equation 1 and reducing:
D -296X200X2992xf^§ ^\ 0-00126 X 100' X 960 X 0.016 X 200
^a - ^b x zw x ^y.y^ x ^ 522 - 960 j 1Q6 x 29 92 x 0 09
= 1.27 - 0.14 = 1.13 in.
Fig. 4 shows the variation in the available draft of a typical 200 ft by
10 ft chimney operating under the general conditions noted in Example 1.
When the chimney is under static conditions and no gases are flowing, the
available draft is equal to 1.27 in. of water, the theoretical intensity. As
the amount of gases flowing increases, the available intensity decreases
until it becomes zero at a gas flow of 297 Ib per second, at which point the
draft loss due to friction is equal to the theoretical intensity. The draft-
capacity curve corresponds to the head-capacity curve of centrifugal
pump characteristics and the dynamic-head-capacity curve of a fan. The
point of maximum draft and zero capacity is called shut-off draft, or point
of impending delivery, and corresponds to the point of shut-off head of a
centrifugal pump. The point of zero draft and maximum capacity is
called the wide open point and corresponds to the wide open point of a
centrifugal pump. A set of operating characteristics may be developed
for any size chimney operating under any set of conditions by substituting
the proper values in Equation 1 and then plotting the results in the
manner shown in Fig. 4.
The efficiency of a natural draft chimney is the thermodynamical ratio
of the energy output to the energy input. The energy output is the total
426
CHAPTER 26 — CHIMNEYS AND DRAFT CALCULATIONS
work done by the chimney in moving the gases and corresponds to the
water horsepower of a centrifugal pump, or the total work done by a fan
in moving the gases. The energy input is equal to the theoretical amount
of power generated by the chimney and corresponds to the power input
of the driving unit of a centrifugal pump or a fan. The thermodynamical
efficiency is given by the equation:
Et =
A\/H
(2}
where
= a constant depending upon the temperature of the gases, the atmospheric
temperature, the elevation of the plant, and the density and specific heat of the
gases. For average operating conditions, K& — 0.0065.
JU
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.0009
.0008
.0007
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.0005
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) 30 60 90 120 150 180 210 240 270 300
Amount of Gases Flowing and Discharged, Ib. per sec., W
£
i. !y
FIG. 4. TYPICAL SET OF OPERATING CHARACTERISTICS OF A NATURAL DRAFT CHIMNEY
Fig. 4 shows the variation in the efficiency of the chimney under con-
sideration for the operating conditions noted. This curve rises from zero
at shut-off draft to a maximum for a certain draft and its corresponding
capacity and then drops again to zero at the wide open point. The point
of maximum efficiency is located by the point on the draft-capacity curve
equal to two-thirds of the theoretical draft intensity. In Example 1 the
maximum efficiency is at an available draft intensity of % X 1.27 = 0.85
in. of water and the corresponding capacity of 175 Ib per second.
The efficiency curve of a natural draft chimney corresponds to the
efficiency curves of a centrifugal pump and a fan and serves the same
general use in that it locates the region of most economical operation. In
substituting the values for the various factors in Equation 1, care should
be exercised that the selections be as near the actual conditions as is
practically possible. The following notes will serve as a guide for these
selections :
427
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
1. The barometric pressure varies inversely as the altitude of the plant above sea level.
Fig. 5 gives the barometric pressure corresponding to various elevations as computed
from the equation:
where
62,737 log -
altitude of plant above sea level, feet.
(3)
In general, the barometric pressure decreases approximately 0.1 in. of mercury per 100
ft increase in elevation.
2. The unit weight of a cubic foot of chimney gases at 0 F and sea level barometric
pressure is given by the equation :
Wc = 0.131 CO* + 0.095
0.083
(4)
29
^28
*o
c 27
OJ
= 26
J-25
'= 24
| 23
CO
CD 22
21
?n
\
^x
N
\
^»s_
^v
.
\
^x
\
^
k^
-^
0 1000 2000 3000 4000 5000 6000 7000
Corresponding Altitude above Sea Level, ft
FIG. 5. RELATION BETWEEN BAROMETRIC PRESSURE AND ALTITUDE
In this equation CO?, 0% and Ns represent the percentages of the parts by weight of the
carbon dioxide, oxygen and nitrogen content, respectively, of the gas analysis. For
ordinary operating conditions, the value of W^ may be assumed at 0.09.
3. The atmospheric temperature is the actual observed temperature of the outside air
at the time the analysis of the operating chimney is made. The mean atmospheric
temperature in the temperate zone is approximately 62 F.
4. The chimney gas temperature does not vary appreciably from the gas temperature
as it leaves the breeching and enters the chimney. For average operating conditions, the
chimney gas temperature will vary between 500 F and 650 F except in the case when
economizers and recuperators are used, when the temperature will vary between 300 F
and 450 F. If a chimney has been properly constructed, properly lined and has no air
infiltration due to open joints, the temperature of the gases throughout the chimney will
not differ appreciably from the foregoing figures. In most up-to-date heating plants, the
temperature may be read from instruments or ascertained from a pyrometer.
5. The coefficient of friction between the chimney gases and a sooted surface has been
found to be approximately 0.016. This factor, of course, will be much less for a new
unlined steel stack than for a brick or brick-lined chimney, but in time the inside surface
of all chimneys regardless of the material of which they are constructed becomes covered
with a layer of soot and the coefficient of friction should be the same for all types of
chimneys.
6. The length of the friction duct is the vertical distance between the bottom of the
breeching opening and the top of the chimney. Ordinarily this distance is approximately
equal to the height of the chimney above the grate level.
428
CHAPTER 26 — CHIMNEYS AND DRAFT CALCULATIONS
7. The amount of gases flowing and being discharged is, of course, equal to the amount
of gases generated in the combustion chamber of the boiler. The total products of
combustion may be computed from the equation:
W
where
CgGWtp
3600
Cg = pounds of fuel burned per square foot of grate surface per hour.
G = total grate surface of boilers, square feet,
f/tp = total weight of products of combustion per pound of fuel.
(5)
.001 .002 .003 .004 .005 .006 .007
Available Draft per Ft. of Height, in. of Water
FIG, 6. CHIMNEY PERFORMANCE CHART
Fig. 6 is a typical chimney performance chart giving the available draft
intensities for various amounts of gases flowing and sizes of ^ chimney.
This chart is based on an atmospheric temperature of 62 F, a chimney gas
temperature of 500 F, a unit chimney gas weight of 0.09 Ib per cubic foot,
sea level atmospheric pressure, a coefficient of friction of 0.016, and a
friction duct length equal to the height of the chimney above the grate
level. These curves may be used for general operating conditions. For
specific operating conditions, a new chart should be constructed from
Equation 1.
It has been the usual custom, and still is to a lamentably igreat extent,
to select the required size of a natural draft chimney from a table of
429
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
chimney sizes based only on boiler horsepowers. After the ultimate
horsepower of the projected plant had been determined, the chimney size
in the table corresponding to this figure was then selected as the proper
size required. Generally, no further attempt was made to determine if
the height thus selected was sufficient to help create the required draft
demanded by the entire installation, or the diameter sufficiently large to
enable the chimney quickly, efficiently, and economically to dispose of the
gases. Since the operating characteristics of a natural draft chimney are
similar in all respects to those of a centrifugal pump, or a centrifugal fan,
it is no more possible to select a proper size chimney from such a table,
even with correction factors appended, than it is to select the proper size
pump from tables based only on the amount of water to be delivered.
DETERMINING CHIMNEY SIZES
The required diameter and height of a natural draft chimney are given
by the following equations:
A-
D = 0.288 J WTc ('}
1 BoWcV
where
H — required height of chimney above grate bar level, feet.
D = required minimum diameter of chimney, feet.
V = chimney gas velocity, feet per second.
DT = total required draft demanded by the entire installation outside of the chimney,
inches of water.
Equations 6 and 7 give the required size of a natural draft chimney with
all of the operating factors taken into consideration. Values for all of the
factors with the exception of the chimney gas velocity may be either
observed or computed. It is, of course, necessary to assume an arbitrary
value for the velocity in order to arrive at some definite size. For any one
set of operating conditions there will be as many sizes of chimneys as there
are values of reasonable velocities to assume. Of the number of sizes
corresponding to the various assumed velocities, there is one size which
will cost least. Since the cost of a chimney structure, regardless of the
kind of material used in the construction, varies as the volume of material
in the structure, the cost criterion then may be represented by the
approximate equation:
Q = *tHD (8)
where
Q — volume of material, cubic feet.
/ = average wall thickness, feet.
For all practical purposes, the value of nt may be taken as a constant
regardless of the size of the structure. Hence, in general, the voluine, and
consequently the cost, of a chimney structure may be based on the factor
430
CHAPTER 26 — CHIMNEYS AND DRAFT CALCULATIONS
HD as a criterion. Therefore, the value of the chimney gas velocity which
will result in the least value of HD for any one set of operating con-
ditions will produce a structure which will be the most economical to use,
because its cost will be least.
The problem at hand is to deduce an equation for the chimney gas
velocity which will result in a combination of a height and a diameter
whose product HD will be least. The solution is obtained by equating the
200
190
180
170
^.160
§150
&140
£
•g-130
|120
|no
"glOO
| 90
1 80
1 7°
I 60
| 50
| 40
30
20
10
°(
Height of Chimney, ft.
D 25 50 7510012515017520022525027530032535037
2.0
1.9
1.8
1.7
1.6
1.5
W ,
13?-
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ay I
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) 1 2 3 4 5 6 7 8 9 10 11 12 13 14 1
Diameter of Chimney, ft.
FIG. 7. ECONOMICAL CHIMNEY SIZES
product of Equations 3 and 4 to HD, differentiating this product with
respect to V and equating the resulting expression to zero. This pro-
cedure results in the following expression :
2/5
(9)
where Fe ~ economical chimney gas velocity, feet per second.
Equation 9 gives the economical velocity of the chimney gases for any
set of 'Operating conditions, and represents the velocity which will result in
a chimney the size of which will cost less than that of any other size as
determined by any other velocity for the same operating conditions.
After the value of the economical velocity has been determined, the
431
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
corresponding height and diameter can then be determined from Equa-
tions 6 and 7, respectively, and the economical size will then be attained.
Equations 6, 7 and 9 may be simplified considerably for average operating
conditions in an average size steam plant by assuming the following
conditions:
Average chimney gas temperature, 500 F Tc = 960
Mean atmospheric temperature, 62 F T0 = 522
Average coefficient of friction, 0.016 ./ = 0.016
Average chimney gas density, 0.09 Wc = 0.09
Sea level elevation with barometer of 29.92 B0 - 29.92
Substituting these values in Equations 9, 7 and 6, respectively, and
reducing:
7e
D
H = 190Dr (12)
Fig. 7 gives the economical chimney sizes for various amounts of gases
flowing and for required draft intensities as computed from Equations 10,
11 and 12. They are based on the operating factors used in reducing
Equations 6, 7 and 9 to their simpler form. The sizes shown by the
curves in the chart should be used for general operating conditions only,
or for installations where the required data necessary for an exact deter-
mination are difficult or impossible to secure. Whenever it is possible to
secure accurate data, or the anticipated operating conditions are fairly
well known, the required size should be determined from Equations 6,
7 and 9. The recommended minimum inside dimensions and heights of
chimneys for small and medium size installations are given in Table 1.
GENERAL EQUATION
The general draft equation for a steam producing plant may be stated
as follows:
Dt - hf = to -f AB + h*d 4- he 4- hBr + hv + ho -1- k& + £R (13)
where
Dt = theoretical draft intensity created by pressure transformer, inches of water.
h{ — draft loss due to friction in pressure transformer, inches of water,
/rp = draft loss through the fuel bed, inches of water.
/ZB == draft loss through the boiler and setting, inches of water.
h%T = draft loss through the breeching, inches of water.
hv = draft loss due to velocity, inches of water.
^Bd = draft loss due to bends, inches of water.
he = draft loss due to contraction of opening, inches of water.
ho = draft loss due to enlargement of opening, inches of water.
&E — draft loss through the economizer, inches of water.
&R = draft loss through recuperators, regenerators, or air heaters, inches of water.
The left hand member of Equation 13 represents the total amount of
available draft created by the pressure transformer, that is, the natural
432
CHAPTER 26 — CHIMNEYS AND DRAFT CALCULATIONS
TABLE 1.
RECOMMENDED MINIMUM CHIMNEY SIZES FOR
HEATING BOILERS AND FURNACES a
H.-_
RECTANGULAR FLUE
ROUND FLUE
WARM Am
FURNACE
CAPACITY
IN SQ Lv.
OF LEADER
STEAM
BOILER
CAPACITY
SQ FT
OP RADI-
ATION
OT
WATER
HEATER
CAPACITY
SQFT
OF RADI-
ATION
NOMINAL
DIMEN-
SIONS OP
FIRE CLAY
LINING
IN INCHES
HEIGHT
IN FT
ABOVE
GRATE
Actual
Inside
Dimensions
of Fire Clay
t Lining
Actual
Area
Sq In.
Inside
Diam-
eter of
Lining
in
Actual
Area
Sq In.
in Inches
Inches
790
590
973
8j^x 13
7 X ll/^
81
35
1000
690
1,140
10
79
900
1,490
13x13
113^ x llj^
127
900
1,490
83^x18
65^ x 16/<£
110
1,100
1,820
12
113
40
1,700
2,800
13x18
llj^x 16J4
183
1,940
3,200
15
177
2,130
3,520
18x18
15^x15%
248
2,480
4,090
20x20
298
45
3,150
5,200
18
254
50
4,300
7,100
20
314
4,600
7,590
20x24
17x21
357
5,000
8,250
24x24
21x21
441
55
5,570
9,190
24x24t>
576
60
5,580
9,200
22
380
6,980
11,500
24
452
65
7,270
12,000
24x28t>
672
8,700
14,400
28x28^
784
9,380
15,500
27
573
10,150
16,750
30x30^
900
10,470
17,250
28x32b
896
aThis table is taken from the A.S.H.V.E. Code of Minimum Requirements for the Heating and Venti-
lation of Buildings (Edition of 1929).
bDimensions are for unlined rectangular flues.
draft chimney, Venturi chimney, or fan, and is equal to the theoretical
intensity less the internal losses incidental to operation. The right hand
member represents the sum of all of the various losses of draft throughout
the entire boiler plant installation outside of the pressure transformer
itself. The left hand member expresses the available intensity and is
analogous to the head developed by a centrifugal pump in a water works
system, while the right hand member expresses the required draft in-
tensity and is analogous to the total dynamic head in a water works
system. For a general circulation of gases
£>a - Dr (14)
where
DT
available draft intensity, inches of water.
> required draft, inches of water.
The draft loss through the fuel bed (Ap)> or the amount of draft required to
effect a given or required rate of combustion, varies between wide limits
and represents the greater portion of the required draft. In coal-fired
installations, the draft loss through the fuel bed is dependent upon the
following factors: (1) character and condition of the fuel, clean or dirty;
(2) percentage of ash in the fuel; (3) volume of interstices in the fuel bed, ,
433
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
coarseness of fuel; (4) thickness of the fuel bed, rate of combustion;
(5) type of grate or stoker used; (6) efficiency of combustion.
There is a certain intensity of draft with which the best results will be
obtained for every kind of coal arid rate of combustion. Fig. 8 gives the
intensity of draft, or the vacuum in the combustion chamber required to
burn various kinds of coal at various rates of combustion. Expressed in
other words, these curves represent the amount of draft required to force
the necessary amount of air through the fuel bed in order to effect various
rates of combustion. It will be noted that the amount of draft increases
as the percentage of volatile matter diminishes, being comparatively low
for the lower grades of bituminous coals and highest for the high grades
and small sizes of anthracites. Also, when the interstices of the coal are
large and the particles are not well broken up, as with bituminous coals,
05 10 15 £0 25 30 35 40 45
Pounds of Coal Burned per 5<7|.Ft of Grctte Surface per Hr:
FIG. 8. DRAFT REQUIRED AT DIFFERENT RATES OF COMBUSTION
FOR VARIOUS KINDS OF COAL
much less draft is required than when the particles are small and are well
broken up, as with bituminous slack and the small sizes of anthracites. In
general, the draft loss through the fuel bed increases as: (1) the per-
centage of volatile matter diminishes; (2) the percentage of fixed carbon
increases; (3) the thickness of the bed increases; (4) the percentage of ash
increases; (5) the volume of the interstices diminishes.
In making the preliminary assumptions for the draft loss through the
fuel bed, due allowances should be made for a possible future change in
the grade of fuel to be burned and also in the rate of combustion. A value
should be selected for this loss which will represent not only the highest
rate of combustion which will be encountered, but also the grade of coal
which has the greatest resistance through the fuel bed and which may be
burned at a later date.
In powdered-fuel and oil-fired installations, there will be no draft loss
434
CHAPTER 26 — CHIMNEYS AND DRAFT CALCULATIONS
through the fuel bed since there is none and, consequently, this factor
becomes zero in the general draft equation. All other factors being
constant, the height of the chimney in installations of this character will
be less than the height in coal-fired Installations, and in the case of me-
chanical draft installations the driving units need not be as large since the
head against which the fan is to operate is not as great in the former as
in the latter.
The draft loss through the boiler and setting (h%) also varies between wide
limits and, in general, depends upon the following factors:
1. Type of boiler. 5. Arrangement of baffles.
2. Size of boiler. 6. Type of grate.
3. Rate of operation. 7. Design of brickwork setting.
4. Arrangement of tubes. 8. Excess air admitted.
9. Location of entrance into breeching.
Curves showing the draft loss through the boiler are usually based on
the load or quantity of gases passing through the boiler, expressed in
terms of percentage of normal rate of operation. Owing to the great
variety of boilers of different designs and the various schemes of baffling,
it is impossible to group together a set of curves for the draft loss through
the boiler which may even be used generally. It is therefore necessary to
secure this information from the manufacturer of the particular type of
boiler and baffle arrangement under consideration.
When a boiler is installed and in operation, the draft loss depends upon
the amount of gases flowing through it. This, in turn, depends upon the
proportion of excess air admitted for combustion. The amount of excess
air is measured by the C02 content; the less the amount of C02, the
greater the amount of excess air and hence the greater the draft loss.
The loss of draft through the boiler will vary directly as the size of the
boiler and the length of the gas passages within. The loss also varies as
the number of tubes high, but not in a direct ratio inasmuch as the loss
due to the reversal of flow at the ends of the baffles remains constant
regardless of the height of the boiler. The arrangement of the tubes,
whether the gases flow parallel to or at right angles to the tubes, has an
appreciable effect on the loss. The arrangement of the baffles influences
the draft loss greatly, the loss through a boiler with five passes being
greater than the loss through one of three or four passes. A poor design
arid a rough condition of the brickwork will increase the loss greatly,
whereas a proper design and a smooth condition will keep the loss at a
minimum. The loss through the boiler will be less when the breeching
entrance is located at or near the top of the boiler than when it is located
at or near the bottom since the gases have a shorter distance to travel
in the former instance.
1 The draft loss through the breeching (/br) is given by the general
equation :
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
where
W = the amount of gases flowing, pounds per second.
Tc = absolute temperature of breeching gases, degrees Fahrenheit.
/ = coefficient of friction.
L — length of breeching, feet.
A — area of breeching, square feet.
BQ = atmospheric pressure corresponding to altitude, inches of mercury.
Wc = weight of a cubic foot of breeching gases at 0 F and sea level atmospheric
pressure, pounds per cubic foot.
Cbr = hydraulic radius of breeching section.
It has been the general custom to lump off the intensity of the breeching
loss at 0.10 in. of water per 100 ft of breeching length regardless of its size
or shape or the amount and temperature of the gases flowing through it.
This practice is hazardous and has no more foundation in fact than that of
determining the friction head in a water works system without taking
into consideration the size of the pipe or the amount of water flowing
through it. When the length of the breeching is relatively short, any
variation in any one of the factors in the equation will have no appreciable
effect on the draft loss. However, when the breeching is relatively long,
the draft loss is affected greatly by the various factors, particularly by the
size and shape as well as by the weight of gases flowing.
The draft loss due to velocity (hv) is given by the equation
and represents the amount of draft required to accelerate the gases from
zero velocity to the velocity at which the gases are flowing, or in other
words, from a static gas condition of zero flow to the amount of gases
flowing throughout the installation. This loss corresponds to the velocity
head in water works systems.
The draft loss due to bends (&sd) is equivalent to the loss due to the
velocity head for a 90-deg bend. In changing direction of flow, the gas
velocity decreases to zero with a loss of velocity head and then increases
to its proper value at the expense of a loss in pressure head, the net result
being a loss in pressure head equal to the velocity head at the bend.
This loss is given by the equation :
, 0.000194 W*TC /.~v
The friction at a right-angle bend is sometimes expressed as the
equivalent of a straight length of flue of a certain length for a certain
diameter, similar to the procedure used in estimating the loss due to
bends in piping systems conducting water. Most flues, however, par-
ticularly breechings, are built square or rectangular in section and no
general equation based on the shape of the flue can be conveniently
expressed.
The draft loss due to sudden contraction of an area (he) is given by the
equation :
436
CHAPTER 26 — CHIMNEYS AND DRAFT CALCULATIONS
.
he = ,,2R T,7 (18)
Kc = coefficient of sudden contraction based on -— , the ratio of the areas of the
•"•i
smaller to the larger section.
As = area of the smaller section.
When the flue or passage through which the gases flow is suddenly
contracted, a considerable portion of the static head in the larger section
is converted into velocity head and a draft loss of some consequence, par-
ticularly in a short breeching, takes place. A sudden contraction should
always be avoided where possible. At times, however, due to obstruc-
tions or limited head-room, it is necessary to alter the size of the breeching,
but a sudden contraction may be avoided by gradually decreasing the
area over a length of several feet.
The draft loss due to a sudden enlargement of an area (ho) is given by the
equation :
0.000194£0 J7*rc
h° - AlBoW* - (19)
where
A
KO = coefficient of sudden enlargement based on -~, the ratio of the areas of the
A\
smaller to the larger section.
When the flue or passage through which the gases flow is suddenly
enlarged, a portion of the velocity head is converted into static head in the
larger section and, like the loss due to sudden contraction, a loss of some
consequence, particularly in short breechings, takes place. A sudden
enlargement in a breeching may be avoided by gradually increasing the
area over a length of several feet. In large masonry chimneys, the area of
the flue at the region of the breeching entrance is considerably larger
than the area of the breeching at the chimney, and a sudden enlargement
exists.
The draft loss through the economizer (fe) should be obtained from the
manufacturer but for general purposes it may be computed from the
following general equation:
te - "c (20)
10™
where
Wn = pounds of gases flowing per hour per linear foot of pipe in each economizer
section.
N =s number of economizer sections.
An economizer in a steam plant affects the draft in two ways, (1) it
offers a resistance to the flow of gases, and (2) it lowers the average
chimney gas temperature, thereby decreasing the available intensity. In
the case of a natural draft installation, both of these factors result in a
relative increase in the height of the chimney and, in the case of a large
437
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
plant, they may add as much as 20 or 30 ft to the height. The decrease
in the temperature of the gases after they have passed through the
economizer has an extremely important effect on the performance of a
natural draft chimney and also upon the performance of a fan.
CONSTRUCTION DETAILS
For general data on the construction of chimneys reference should be
made to the Standard Ordinance for Chimney Construction of the
National Board of Fire Underwriters. Briefly summarized, these provisions
are as follows for heating boilers and furnaces :
The construction, location, height and area of the chimney to which a heating boiler
or warm-air furnace is connected affect the operation of the entire heating system. Most
residence chimneys are built of brick and may be either lined or unlined, but in either
case the walls must be air-tight and there should be only one smoke opening into the
chimney. Cleanout, if provided, must be absolutely air-tight when closed.
The walls of brick chimneys shall be not less than 3J£ in. thick (width of a standard
size brick) and shall be lined with fire-clay flue lining. Fire-clay flue linings shall be
manufactured from suitable refractory clay, either natural or compounded, and shall
be adapted to withstand high temperatures and the action of flue gases. They shall be
of standard commercial thickness, but not less than % in- All fire-clay flue linings shall
meet the standard specification of the Eastern Clay Products Association. The flue
sections shall be set in special mortar, and shall have the joints struck smooth on £he
inside. The masonry shall be built around each section of lining as it is placed, and all
spaces between masonry and linings shall be completely filled with mortar. No broken
flue lining shall be used. Flue lining shall start at least 4 in. below the bottom of smoke-
pipe intakes of flues, and shall be continued the entire heights of the flues and project
at least 4 in. above the chimney top to allow for a 2 in. projection of lining. The wash or
splay shall be formed of a rich- cement mortar. To improve the draft the wash surface
should be concave wherever practical.
Flue lining may be omitted in brick chimneys, provided the walls of the chimneys
are not less than 8 in. thick, and that the inner course shall be a refractory clay brick.
All brickwork shall be laid in spread mortar, with all joints push-filled. Exposed joints
both inside and outside shall be struck smooth. No plaster lining shall be permitted.
Chimneys shall extend at least 3 ft above flat roofs and 2 ft above the ridges of peak
roofs when such flat roofs or peaks are within 30 ft of the chimney. The chimney
shall be high enough so that the wind from any direction shall not strike the top of the
chimney from an angle above the horizontal. The chimney shall be properly capped with
stone, terra cotta, concrete, cast-iron, or other approved material; but no such cap
or coping shall decrease the flue area.
There shall be but one connection to the flue to which the boiler or furnace smoke-
pipe is attached. The boiler or furnace smoke-pipe shall be thoroughly grouted into the
chimney and shall not project beyond the inner surface of the flue lining.
The size or area of flue lining or of brick flue for warm-air furnaces depends on height
of chimney and capacity of heating system. For chimneys not less than 35 ft in height
above grate line, the net internal dimensions of lining should be at least 7x 11 J^ in.
for a total leader pipe area up to 790 sq in. Above 790 and up to 1,000 sq in. of leader
pipe area the lining should be at least 11 Ji x 11 M in. inside. In case of brick flues not
less than 35 ft in height with no linings, the internal dimensions should be at Isast
8 x 12 in. up to 790 sq in. of leader area, and at least 12 x 12 in. for leader capacities up to
1,000 sq in. Chimneys under 35 ft in height are unsatisfactory in operation and hence
should be avoided. . N '
CHIMNEYS FOR CAS HEATING
The burning of gas differs from the burning of coal in that the force
which supplies the air for combustion of the gas comes largely from the
pressure of the gas in the supply pipe, whereas air is supplied to a bedtoi
438
CHAPTER 26 — CHIMNEYS AND DRAFT CALCULATIONS
burning coal by the force of the chimney draft. If, with a coal-burning
boiler, the draft is poor, or if the chimney is stopped, the fire is smothered
and the combustion rate reduced. In a gas boiler or furnace such a
condition would interfere with the combustion of the gas, but the gas
would continue to pass to the burners and the resulting incomplete com-
bustion would produce a dangerous condition. In order to prevent incom-
plete combustion from insufficient draft, all gas-fired boilers and furnaces
should have a back-draft diverter in the flue connection to the chimney.
A study of a typical back-draft diverter (Fig. 9) shows that partial' or
complete chimney stoppage will merely cause some of the products of
combustion to be vented out into the boiler room, but will not interfere
with combustion. In fact, gas-designed appliances must perform safely
--r
-h,
FIG. 9. TYPICAL BACK-DRAFT DIVERTER
under such a condition to be approved by the American Gas Association
Laboratory. Other functions of the back-draft diverter are to protect the
burner and pilot from the effects of down-drafts, and to neutralize the
effects of variable chimney drafts, thus maintaining the appliance ef-
ficiency at a substantially constant value. Converted boilers or furnaces,
as well as gas-designed appliances, should be provided with back-draft
diverter s.
As is the case with the complete combustion of almost all fuels, the
products of combustion for gas are carbon dioxide (CO 2) and water vapor
with just a trace of sulphur trioxide (503). Sulphur usually burns to the
trioxide in the presence of an iron oxide catalyst. The volume of water
vapor in the flue products is about twice the volume of the carbon dioxide
when coke oven or natural gas is burned. Because of the large quantity
of water vapor which is formed by the burning of gas, it is quite important
that all gas-fired central heating plants be connected to a chimney having
a good draft. Lack of chimney draft causes stagnation of the proiducts of
combustion in the chimney and results in the condensation of a large
amount of the water vapor. A good chimney draft draws air into the
chimney through the openings in the back-draft diverter, lowers the dew
point of the mixture, and reduces the tendency of the water vapor to
condense. ;
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
A chimney for a gas-fired boiler or furnace should be constructed in
accordance with the principles applicable to other boilers. Where the
wall forming a smoke flue is made up of less than an 8-in. thickness of
brick, concrete, or stone, a burnt fire clay flue tile lining should be used.
Care should be used that the lengths of flue tile meet properly with no
openings at the joints. Cement mortar should be used for the entire
chimney.
TABLE 2. MINIMUM ROUND CHIMNEY DIAMETERS FOR GAS APPLIANCES (INCHES)
HEIGHT or
GAS CONSUMPTION JN THOUSANDS OP BTTT PER HOUR
UHIMNBY
FEET
100
200
300
400
500
750
1000
1500
2000
20
4.50
5.70
6.60
7.30
8.00
9.40
10.50
12.35
13.85
40
4.25
5.50
6.40
7.10
7.80
9.15
10.25
12.10
13.55
60
4.10
5.35
6.20
6.90
7.60
8.90
10.00
11.85
13.25
80
4.00
5.20
6.00
6.70
7.35
8.65
9.75
11.50
12.85
100
3.90
5.00
5.90
6.50
7.20
8.40
9.40
11.00
12.40
Table 2 gives the minimum cross-sectional diameters of round chim-
neys (in inches) for various amounts of heat supplied to the appliance,
and for various chimney heights. This is in accordance with American
Gas Association recommendations.
The flue connections from a gas-fired boiler or furnace to the chimney
should be of a non-corrosive material. In localities where the price of
gas requires the use of highly efficient appliances, the material used for
the flue connection not only should be resistant to the corrosion of water,
but should resist the corrosion of dilute solutions of sulphur trioxide in
water. Sheet aluminum, as well as some other materials, seems to serve
this purpose very well.
PROBLEMS IN PRACTICE
1 • What is draft?
Draft is an unbalanced pressure between the atmosphere and the passages in the ap-
paratus or construction through which the gases flow.
2 • What two kinds of draft need be considered?
Natural draft caused by temperature differences, and artificial draft caused by me-
chanical forcing.
3 • What is the effective height of a chimney?
The height from the grate level to the top of the chimney is the effective height in pro-
ducing natural draft.
4 • What dual purpose does a tall chimney fulfill?
A tall chimney primarily creates the necessary draft to move the air required for the
combustion process and to move the products of combustion, and secondarily it dis-
charges the gases at a high elevation to prevent them from becoming a nuisance.
440
CHAPTER 26 — CHIMNEYS AND DRAFT CALCULATIONS
5 • a. Name the principal advantages of natural draft.
b. Name the principal disadvantages of natural draft.
a. Simplicity, reliability, freedom from mechanical parts, low cost of maintenance,
relatively long life, relatively low depreciation, operation with no power requirement.
i>. Lack of flexibility, irregularity, dependence on surroundings, susceptibility to tem-
perature changes.
6 • How is mechanical draft created?
By forced draft, by induced-draft fans, or by a Venturi chimney.
7 • Distinguish between theoretical and available draft.
Theoretical draft is the difference in pressure inside and outside the base of a chimney
when it is under operating temperatures but when there are no gases flowing. Available
draft is less than theoretical draft by the friction loss due to the flow of gases through
the chimney.
8 • Explain the term efficiency of a natural draft chimney.
The efficiency of a chimney is the ratio of the work it does in moving gases to the theo-
retical amount of power it generates.
9 • How is the available draft used in a heating plant?
The available draft at the base of the chimney is used to overcome the loss in pressure
through the grate, the fuel bed, the boiler passes, the breeching, and the chimney.
10 • What are some of the factors that influence the draft loss through the fuel
bed?
Uniformity and size of coal, the amount of ash mixed with the fuel on the grate, thickness
of fuel bed, rate of combustion, amount of air supply as related to the coal burning rate.
11 • How does the volatile matter content affect the draft loss through the fuel
bed?
The higher the volatile content and the lower the fixed carbon content, the lower the
draft loss.
12 • In what cases will there be no fuel bed draft loss?
In oil, gas, and powdered fuel firing the fuel is mixed and burned in suspension; con-
sequently, no measurable resistance is encountered in the combustion zone.
13 • Is it possible to state an average value for the draft loss through a boiler
and its setting?
No. The draft loss varies widely and depends on many factors such as the size and type
of gas passageways. The manufacturer is usually able to supply such information.
14 • Of what significance is the CO2 content of stack gases in establishing
draft loss?
The CO2 content of the exit gases is a measure of the completeness of the combustion and
the amount of excess air supplied. Low CO* indicates a high excess of air and hence
a high draft loss.
15 • "What two effects does an economizer have on the draft loss?
An economizer offers resistance to the flow of gases over the added surfaces; it lowers the
temperature of the gases going to the chimney and therefore decreases the available
draft. This decrease often necessitates the addition of forced draft.
16 • What main provisions should be considered in good chimney construction?
Chimneys should be air-tight and connected to only one smoke opening. The chimney
top should be high enough above surroundings so the wind will not strike it at any angle
441
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
above the horizontal. Chimney walls should be not less than one brick in width, and
they should be lined with fire clay tile of the size required for the attached heating unit.
Tile lining sizes are stated as outside dimensions; therefore, their effective dimensions
are less by the thickness of the wall.
17 • Wnat is the purpose of a back draft diverter as used on gas burning units?
Since the fuel is supplied under pressure independent of draft it is necessary to free the
unit from the variable chimney draft and to supply air for combustion in direct propor-
tion to the supply of fuel gas. The back draft diverter protects the pilot and burners
from down drafts.
442
Chapter 27
FUELS AND COMBUSTION
Classification of Coaly Air for Combustion, Draft Required, Com-
bustion of Anthracite, Firing Bituminous Coal, Burning Coke,
Hand Firing, Classification and Use of Oil, Classification and
Use of Gas
THE choice of fuel for heating is a question of economy, cleanliness,
fuel availability, operation requirements, and control. The principal
fuels to be considered are coal, oil, and gas.
COAL
The complex composition of coal makes it difficult to classify it into
clear-cut types. Its chemical composition is some indication but coals
having the same chemical analysis may have distinctly different burning
characteristics. Users are mainly interested in the available heat per
pound of coal, in the handling and storing properties, and in the burning
characteristics. A description of the relationship between the qualities
of coals and these characteristics requires considerable space; a treatment
applicable to heating boilers is given in U. S. Bureau of Mines Bulletin 276.
A classification of coals is given in Table 1, and a brief description of the
kinds of fuels is given in the following paragraphs, but it should be
recognized that there are no distinct lines of demarcation between tbf
kinds, and that they graduate into each other:
Anthracite is a clean, dense, hard coal which creates very little dust in handling. It
is comparatively hard to ignite but it burns freely when well started. It is non-caking,
it burns uniformly and smokelessly with a short flame, and it requires little attention to
the fuel beds between firings. It is capable of giving a high efficiency in the common
types of hand-fired furnaces.
Semi-anthracite has a higher volatile content than anthracite, it is not as hard and
ignites somewhat more easily; otherwise its properties are similar to those of anthracite.
Semi-bituminous coal is soft and friable, and fines and dust are created by handling it.
It ignites somewhat slowly and burns with a medium length of flame. Its caking prop-
erties increase as the volatile matter increases, but the coke formed is relatively weak.
Having only half the volatile matter content of the more abundant bituminous coals it
can be burned with less production of smoke, and it is sometimes called smokeless coal.
The term bituminous coal covers a large range of coals and includes many types having
distinctly different composition, properties, and burning characteristics. The coals range
from the high-^rade bituminous coals of the East to the poorer coals of the West. Their
caking properties range from coals which completely melt, to those from which the
volatiles and tars are distilled without change of form, so that they are classed as non-
caking or free-burning. Most bituminous coals are strong and non-friable enough to
permit of the screened sizes being delivered free from fines. In general, they ignitk
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
easily and burn freely; the length of flame varies with different coals, but it is long. Much
smoke and soot are possible especially at low rates of burning.
Sub-bituminous coals occur in the western states; they are high in moisture when
mined and tend to break up as they dry or when exposed to the weather; they are liable
to ignite spontaneously when piled or stored. They ignite easily and quickly and have a
medium length flame, are non-caking and free-burning; the lumps tend to break into
small pieces if poked; very little smoke and soot are formed.
Lignite is of woody structure, very high in moisture as mined, and of low heating
value; it is clean to handle. It has a greater tendency than the sub-bituminous coals to
disintegrate as it dries, and it also is more liable to spontaneous ignition. Freshly mined
lignite, because of its high moisture, ignites slowly. It is non-caking. The char left after
the moisture and volatile matter are driven off burns very easily, like charcoal. The
lumps tend to break up in the fuel bed and pieces of char falling into the ash pit continue
to burn. Very little smoke or soot is formed.
Coke is produced by the distillation of the volatile matter from coal. The type of
coke depends on the coal or mixture of coals used, the temperatures and time of distil-
lation and, to some extent, on the type of retort or oven; coke is also produced as a
residue from the destructive distillation of oil.
Legend: F.C.
TABLE 1. CLASSIFICATION OF COALS BY RANK/
Fixed Carbon. V.M. = Volatile Matter. Btu = British thermal units.
CLASS
GROUP
LIMITS OP FIXED CARBON on BTU
MINERAL-MATTBR-FREE BASIS
REQUISITE PHYSICAL
PROPERTIES
1. Meta-anthracite
Dry F.C., 98 per cent or more (Dry
V.M., 2 per cent or less)
2. Anthracite
Dry F.C., 92 per cent or more and less
I. Anthracite
than 98 per cent (Dry V.M., 8 per
3. Semi-anthracite
cent or less and more than 2 per cent)
Dry F.C., 86 per cent or more and less
Non-agglutinating*
than 92 per cent (Dry V.M.,. 14 per
cent or less and more than 8 per cent)
1. Low volatile bituminous coal
Dry F.C., 77 per cent or more and less
than 86 per cent (Dry V.M., 23 per
cent or less and more than 14 per
cent)
2. Medium volatile bituminous coal
Dry F.C., 69 per cent or more and less
than 77 per cent (Dry V.M., 31 per
cent or less and more than 23 per
II. Bituminous6™
cent)
3. High volatile A bituminous coaL
Dry P.O., leas than 69 per cent (Dry
V.M., more than 31 per cent); and
moist6 Btu, 14,000* or more
4. High volatile B bituminous coal.
Moist6 Btu, 13,000 or more and less
than 14,000*
5. High volatile (7 bituminous coal..
Moist Btu, 11,000 or more and less
Either agglutinating
than 13,000*
or non-weathering*
1. Sub-bituminous A coaL
Moist Btu, 11.000 or more and less
Both weathering and
than 13,000*
non-agglutinating
III. Sub-bituminous..-
2. Sub-bituminous B coaL
Moist Btu 9500 or more and less
than 11, 000*
3. Sub-bituminous C coal
Moist Btu 8300 or more and less
than 9500*
/
1 Lignite
Moist Btu less than 8300
Consolidated
IV. Lignitic <
2. Brown coaL «...
Moist Btu less than 8300
Unconsolidated
fllf agglutinating, classify in low-volatile group of the bituminous class.
*Moist Btu refers to coal containing its natural bed moisture but not including visible water on the
surface of the coal.
"Pending the report of the Subcommittee on Origin and Composition and Methods of Analysis, it is
recognized that there may be non-caking varieties in each group of the bituminous class.
*Cqals having 69 per cent or more fixed carbon on the dry, mineral-matter-free basis shall be classified
according to fixed carbon, regardless of Btu.
•There are three varieties of coal in the High-volatile C bituminous coal group, namely, Variety 1,
agglutinating and non-weathering; Variety 2, agglutinating and weathering; Variety 3, non-agglutinating
and non- weathering.
/Adapted from A.S.T.M. Standards on Coal and Coke, p. 68, American Society for Testing Materials,
Philadelphia, 1934.
444
CHAPTER 27 — FUELS AND COMBUSTION
High-temperature cokes. Coke as usually available is of the high-temperature type,
and contains between 1 and 2 per cent volatile matter. High-temperature cokes are sub-
divided into beehive coke of which comparatively little is now sold for domestic use, by-
product coke, which covers the greater part of the coke sold, and gas-house coke. The
differences among these three cokes are relatively small ; their denseness and hardness
decrease and friability increases in the order named. In general, the lighter and more
friable cokes ignite and burn the more easily.
Low-temperature cokes are produced at low coking temperatures, and only a portion
of the volatile matter is distilled off. Cokes as made by various processes under develop-
ment have contained from 10 to 15 per cent volatile matter. In general, these cokes
ignite and burn more readily than high-temperature cokes. The properties of various
low-temperature cokes may differ more than those of the various high-temperature cokes
because of the differences in the quantities of volatile matter and because some may be
light and others briquetted.
The sale of petroleum cokes for domestic furnaces has been small and is generally
confined to the Middle West. They vary in the amount of volatile matter they contain,
but all have the common property of a very low ash content, which necessitates the
use of refractory pieces to protect the grates from being burned.
In order to obtain perfect combustion a definite amount of air is re-
quired for each pound of fuel fired. A deficiency of air supply will result
in combustible products passing to the stack unburned. An excess of air
absorbs heat from the products of combustion and results in a greater loss
of sensible heat to the stack.
Total Air Required. The theoretical amount of air required per pound
of fuel for perfect combustion is dependent upon the analysis of the fuel ;
TABLE 2. POUNDS OF AIR PER POUND OF FUEL AS FIRED
ANTHRACITE
COKE
SEMI-BITUMINOUS
BITUMINOUS
LIGNITE
9.6
11.2
11.2
10.3
6.2
however, for estimating purposes the theoretical air required for different
grades of fuel may roughly be taken from Table 2. An excess of about
50 per cent over the theoretical amount is considered good practice under
usual operating conditions.
The amount of excess air, based upon the laws of combustion, can be
determined by its relation to the percentage of COz (carbon dioxide) in
the products of combustion. This relationship is shown by the curves
(Fig. 1) for high and low volatile coals and for coke. In hand-fired fur-
naces with long periods between firings the combustion goes through a
cycle in each period and the quantity of excess air present varies.
Secondary Air. The division of the total into primary and secondary
air necessary to produce the same rate of burning and the same excess air
depends on a number of factors which include size of fuel, depth of fuel
bed, and diameter of fire pot. The ratio of the secondary to the primary
air increases with decrease in the size of the fuel pieces, with increase in
the depth of the fuel bed, and with increase in the area of the fire pot; the
ratio also increases with increase in rate of burning.
Size of the fuel is a very important factor in. fixing the quantity of
secondary air required for non-caking coals. With caking coals it is not
445
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
- — — * —
so important because small pieces fuse together and form large lumps.
Fortunately a smaller size fuel gives more resistance to air flow through
the fuel bed and thus automatically causes a larger draft above the fuel
bed, which draws in more secondary air through the same slot openings.
In spite of this, a small size fuel requires a larger opening of the door
slots; for a certain size for each fuel no slot opening is required, and for
larger sizes too much excess air gets through the fuel bed.
It is impossible to establish a single rule for the correct slot opening for
all types and sizes of fuels and for all rates of burning. Furthermore, the
C02, PER CENT
•> fo £ m oo o tv
!\
\\
V
^
s\
s
S\
\\
\
V ^
s\
Pn
ke -
X;
s^^
sV
N
•An
:hra
:ite'
\
\N
V*
\
5x
"S
X.
Low -volatile
jituminous coa
—
**»
^
^
sj^
8
6
v
^s
^
C^
^x
^
High -volatile'
jituminous coa
^*
•>~v
•C;
^1
*-^
^*
^
^
^
^;
"0 20 40 60 80 100 120 140 160
EXCESS AIR, PER CENT
FIG. 1. RELATION BETWEEN CO2 AND EXCESS AIR IN GASES OF COMBUSTION
size of slot opening is dependent on whether the ashpit damper is open
or closed. It is better to have too much than too little secondary air ; the
opening is too small if there is a puff of flame when the firing door is opened.
Fig. 2, taken from the U. S. Bureau of Mines Report of Investigations
No. 2980, shows the relationship of the slot opening, for a domestic fur-
nace, to the size of coke and the rate of burning; these openings are with
the ashpit damper wide open, and would be less if the available draft
permits^of its being partly closed. The same openings are satisfactory for
anthracite.
Bituminous coals require a large amount of secondary air during the
period subsequent to a firing in order to consume the gases and to reduce
the smoke. The smoke produced is a good indicator, and that opening is
best which reduces the smoke to a minimum. Too much secondary air
will cool the gases below the ignition point, and prove harmful instead of
beneficial. The following suggestions will be helpful:
1. In cold weather, with high combustion rates, the secondary air damper should be
half open all the time.
2. In very mild weather, with a very low combustion rate, the secondary air damper
should be closed all the time.
,446
CHAPTER 27 — FUELS AND COMBUSTION
DOOR SLOTS, PER CENT OPEN
? 8 £ 8 8 g
Slots full open
/
,
^
/
/
X
/
/
/
~s~
/
nV
/
/
/
X
r
.>
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1^
4<j
,v
^
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V
x1
s
/
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/
fVi
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X
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/
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X
'
Slo
tad
»ed
— <i
/
/^
/
OP LEAKAGE AROUND
SLOTS AND DOOR
5678.
RATE OF BURNIKG, POUNDS PER SQ. FT. PER HR.
From U. S. Bureau of Mines.
FIG. 2. RELATIVE AMOUNT OF FIRE DOOR SLOT OPENING REQUIRED IN A GIVEN
FURNACE TO GIVE EQUALLY GOOD -COMBUSTION FOR HIGH TEMPERATURE
COKE OF VARIOUS SIZES WHEN BURNED AT VARIOUS RATES
3. For temperatures between very mild and very cold, the secondary air damper
should be in an intermediate position.
4. For ordinary house operation, secondary air is needed after each firing for about
one hour.
Draft Required
The draft required to effect a given rate of burning the fuel as measured
at the smokehood is dependent on the following factors :
1. Kind and size of fuel.
2. Combustion rate per square foot of grate area per hour.
3. Thickness of fuel bed.
4. Type and amount of ash and clinker accumulation.
5. Amount of excess air present in the gases.
6. Resistance offered by the boiler passes to the flow of the gases.
7. Accumulation of soot in the passes.
Insufficient draft will necessitate additional manipulation of the fuel
bed and more frequent cleanings to keep its resistance down. Insufficient
draft also restricts the control by adjustment of the dampers.
The quantity of excess air present has a marked effect on the draft
required to produce a given rate of burning, and it is often possible to
produce a higher rate by increasing the thickness of the fuel bed.
Combustion of Anthracite1
An anthracite fire should never be poked, as this serves to bring ash to
the surface of the fuel bed where it melts into clinker.
Egg size is suitable for large firepots (grates 24 in. and over) if the fuel
*See reports published by The Anthracite Institute Laboratory, Primoa, Pennsylvania.
447
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
can be fired at least 16 in. deep. The air spaces between the pieces of coal
are large, and for best results this coal should be fired deeply.
Stove size coal is the proper size of anthracite for many boilers and
furnaces used for heating buildings. It burns well on grates at least 16 in.
in diameter and 12 in. deep. The only instructions needed for burning
this type of fuel are that the grate should be shaken daily, the fire should
never be poked or disturbed, and the fuel should be fired deeply and
uniformly.
Chestnut size coal is in demand for firepots up to 20 in. in diameter, with
a. depth of from 10 to 15 in.
Pea size coal is often an economical fuel to burn. It is relatively low
in price. When fired carefully, pea coal can be burned on standard grates.
It is well to have a small amount of a larger fuel on hand when building
new fires, or when filling holes in the fuel bed. Care should be taken to
shake the grates only until the first bright coals begin to fall through the
grates. The fuel bed, after a new fire has been built, should be increased
in thickness by the addition of small charges until it is at least level with
the sill of the fire door. This keeps a bed of ignited coal in readiness
against the time when a sudden demand for heat shall be made on the
heater.
Pea size coal requires a strong draft and therefore the best results
generally will be obtained by keeping the choke damper open, the cold-
air check closed, and by controlling the fire with the air-inlet damper only.
Pea size can also be fired in layers with stove or egg size anthracite and
its use in this manner will reduce the fuel costs and attention required.
Buckwheat size coal requires much the same attention as pea size coal,
except that the smaller size of the fuel makes it more difficult to burn on
ordinary grates. Even greater care must be taken in shaking the grates
than with pea coal on account of the danger of the fuel falling through
the grate. A good draft is required and consequently the fire is best
controlled by the air-inlet damper only. Where frequent attention can
be given and where there is not a big heat demand, this fuel is frequently
burned without the aid of any special equipment.
In general it will be found more satisfactory with buckwheat coal to
maintain a uniform heat output and consequently to keep the system
warm all the time, rather than to allow the system to cool off at times
and then to attempt to burn the fuel at a high rate while warming up. A
uniform low fire will minimize the clinker formation and keep the clinker
in an easily broken up Condition so that it readily can be shaken through
the grate.
Forced draft and special grates or retorts frequently are used with this
fuel for best results.
No. 2 buckwheat anthracite, or rice size, is used only with forced draft
equipment on mechanical stokers. No. 3 buckwheat anthracite, or barley,
has no application in domestic heating.
Firing Bituminous Coal
Bituminous coal should never be fired over the entire fuel bed at one
time. A portion of the glowing fuel should always be left exposed to
ignite the gases leaving the fresh charge.
448
CHAPTER 27 — FUELS AND COMBUSTION
Air should be admitted over the fire through a special secondary air
device, or through a slide in the fire door or by opening the fire door
slightly. If the quantity of air admitted is too great the gases will be
cooled below the ignition temperature and will fail to burn. The fireman
can judge the quantity of air to admit by noting when the air supplied
is just sufficient to make the gases burn rapidly and smokelessly above the
fuel bed.
The red fuel in the firebox, before firing, excepting only a shallow layer
of coke on the grate, should be pushed to one side or forward or back-
ward to form a hollow in which to throw the fresh fuel. Some manu-
facturers recommend that all red fuel be pushed to the rear of the firebox
and that the fresh fuel be fired directly on the grate and allowed to ignite
from the top. The object of this is to reduce the early rapid distillation
of gases and to reduce the quantity of secondary air required for smoke-
less combustion.
It is well to have the bright fuel in the firebox so placed that the gases
from the freshly fired fuel, mixed with the air over the fuel bed, pass
over the bed of bright fuel on the way to the flues. The bed of bright
fuel then supplies the heat to raise the mixture of air and gas to the
ignition temperature, thereby causing the gaseous matter to burn and
preventing the formation of smoke.
The fuel bed should be carried as deep as the size of fuel and the
available draft permit, in order to have as much coked fuel as possible
for pushing to the rear of the firebox at the time of firing. A deep fuel
bed allows the longest firing intervals.
If the coal is of the caking kind the fresh charge will fuse into one
solid mass which can be broken up with the stoking bar and leveled from
20 min to one hour after firing, depending on the temperature of the
firebox. Care should be exercised when stoking not to bring the bar up
to the surface of the fuel as this will tend to bring ash into the high
temperature zone at the top of the fire, where it will melt and form
clinker. The stoking bar should be kept as near the grate as possible
and should be raised only enough to break up the fuel. With fuels requir-
ing stoking it may not be necessary to shake the grates, as the ash is
usually dislodged during stoking.
The output obtained from any heater with bituminous coal will usually
exceed that obtainable with anthracite, since soft coal burns more rapidly
than hard coal and with less draft. Soft coal, however, will require
frequent attention to the fuel bed, because it burns unevenly, even
though the fuel bed may be level, forming holes in the fire which admit
too much air, chilling the gases over the fuel bed and reducing the
available draft.
Semi-bituminous coal is fired as bituminous coal, and because of its
caking characteristics it requires practically the same attention. The
Pocahontas Operators Association recommends the central cone method of
firing, in which the coal is heaped on to the center of the bed forming a
cone the top of which should be level with the middle of the firing door.
This allows the larger lumps to fall to the sides, and the fines to remain in
the center and be coked. The poking should be limited to breaking down
the coke without stirring, and to gently rocking the grates. It is recom-
449
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
mended that the slides in the firing door be kept closed, as the thinner fuel
bed around the sides allows enough air to get through.
Burning Coke
Coke is a very desirable fuel and usually will give satisfaction as soon
as the user learns how to control the fire. Coke ignites and burns very
rapidly with less 'draft than anthracite coal. In order to control the air
admitted to the fuel it is very important that all openings or leaks into
the ashpit be closed tightly. A coke fire responds more rapidly than an
anthracite fire to the opening of the dampers. This is an advantage in
warming up the system, but it also makes it necessary to watch the
dampers more closely in order to prevent the fire from burning too rapidly.
A deep fuel bed always should be maintained when burning coke. The
grates should be shaken only slightly in mild weather and should be
shaken only until the first red particles drop from the grates in cold
weather. Since coke weighs only about half as much as anthracite per
cubic foot only about half as much can be put in the firepot, so it will be
necessary to fire oftener. The best size of coke for general use, for small
firepots where the fuel depth is not over 20 in., is that which passes over
a 1 in. screen and through a \Y% in. screen. For large firepots where the
fuel can be fired over 20 in. deep, coke which passes over a 1 in. screen and
through a 3 in. screen can be used, but a coke of uniform size is always
more satisfactory. Large sizes of coke should be either mixed with fine
sizes or broken up before using.
Dustless Coal
The practice of treating the more friable coals to allay the dust they
create is increasing. The coal is sprayed with a solution of calcium
chloride or a mixture of calcium and magnesium chlorides. Both these
salts are very hygroscopic and their moisture under normal atmospheric
conditions keeps the surface of the coal damp, thus reducing the dust
during delivery and in the cellar, and obviating the necessity of sprinkling
the coal in the bin.
The coal is sometimes treated at the mine, but more usually by the
local distributor just before delivery. The solution is sprayed under high
pressure, using from 2 to 4 gal or from 5 to 10 Ib of the salt per ton of
coal, depending on its friability and size.
Pulverized Coal
Installations of pulverized coal burning plants in heating boilers are of
the unit type, in which the pulverized coal is delivered into the furnace
immediately after grinding, together with the proper amount of preheated
air. With this apparatus, where the necessary furnace volume is ob-
tainable, high efficiencies can be obtained.
A 150-hp boiler has generally been considered the smallest size for
which pulverized fuel is feasible. Complications are introduced if an
installation with a single boiler has to take care of very light loads.
Hand Firing
Hand firing is the oldest and the most widely used method of burning
coal for heating purposes. To keep the fuel bed in proper condition where
hand firing is used, the following general rules should be observed :
450
CHAPTER 27 — FUELS AND -COMBUSTION
1. Remove ash from fuel bed by shaking the grates whenever fresh fuel is fired. This
removes ashjrom the fire, enables the air to reach the fuel, and does away with the for-
mation of clinker which is melted ash.
2. Supply the boiler with a deep bed of fuel. Nothing is gained by attempting to
fire a small amount of fuel. A deep bed of fuel secures the most economical results.
3. Remove ash from ashpit at least once daily. Never allow ash to accumulate up
to the grates. If the _ ash prevents the air from passing through, the grate bars will
burn out and much clinker trouble .will be experienced.
The principal requirements for a hand- fired furnace are that it shall have
enough grate area and combustion space. The amount of grate area
required is dependent upon the desired combustion rate.
The furnace volume is influenced by the kind of coal used. Bituminous
coals, on account of their long-flaming characteristic, require more space
in which to burn the gases of combustion completely than do the coals
low in volatile matter. For burning high volatile coals provision should
be made for mixing the combustible gases thoroughly so that com-
bustion is complete before the gases come in contact with the relatively
cool heating surfaces. An abrupt change in the direction of flow tends to
mix the gases of combustion more thoroughly.
OIL
Uniform oil specifications were prepared in 1929 by the American Oil
Burner Association, in cooperation with the American Petroleum Institute,
the U. S. Bureau of Standards, the American Society for Testing Materials
and other interested organizations. Oil fuels were classified into six
groups, as indicated by Table 3. When these specifications were prepared,
it was generally accepted that the first three grades were adapted to
domestic use, while the last three were suitable only for commercial and
industrial burners. Today domestic installations are using No. 4 of the
so-called heavy-oil group, due principally to the fact that No. 4 oils in
general are being offered of better grade and adaptability than those called
for in the commercial specifications.
Since the specifications as originally drawn provide for maximum limits
only for the several grades,^ this differentiation has not proved stable.
Realizing how unsatisfactory it is to have specifications which permit the
substitution of one grade for another, the U. S. Bureau of Standards in
cooperation with the American Society for Testing Materials is figuring
on a new set of specifications providing for definite limits for each grade.
When these specifications are adopted, it is expected that the National
Board of Fire Underwriters will retest all burners using oils of the maximum
specifications for the grade so that if a burner is approved for a certain
grade it will burn any oil meeting the specifications for that particular
grade.
Several burners adapted to industrial use have recently been listed for
automatic operation with No. 5 oil. Usually oils No. 5 or 6 require
preheating for proper operation, but where conditions are favorable, No.
5 can be used without the equipment that this entails.
There are two reasons for the trend to lower grades of oil. While the
lighter oils contain slightly more heat units per pound, the weight per
451
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 3. COMMERCIAL STANDARD FUEL OIL SPECIFICATIONS0
A . Detailed Requirements for Domestic Fuel Oils
GRADE OF OIL
APPROX.
BTU
PER
GAL.&
FLASH POINT
WATER
AND
SEDIMENT,
MAXIMUM
POUR
POINT,*
MAXIMUM
DISTILLATION
TEST
VISCOSITY
MAXIMUM
Min.
Max.
No. 1
Domestic
Fuel Oil
A light distillate
oil for use in
burners requir-
ing a high grade
fuel.
139.000
110 F
or legal
165 F
0.05%
15 F
10% point,
maximum
420 F
End point,
maximum
600 F
No. 2
Domestic
Fuel Oil
A medium distil-
late oil for use
in burners re-
quiring a high
grade fuel.
141.000
125 F
or legal
190 F
0.05%
15 F
10% point,
maximum
440 F
90% point,
maximum
620 F
No. 3
Domestic
Fuel Oil
A distillate fuel
oil for use in
burners where a
low viscosity oil
is required.
143,400
150 F
or legal
200 F
0.1%
15 F
10% point,
maximum
460 F
90% point,
maximum
675 F
Saybolt
Universal
at 100 F
55 seconds
B. Detailed Requirements for Industrial Fuel Oils
GRADE OF OIL
APPROX.
BTU
PER
GAL.*
FLASH POINT,
MIN. MAX.
WATER
AND
SEDIMENT,
MAXIMUM
POUR
POINT,*
MAXIMUM
VISCOSITY,
MAXIMUM
No. 4.
Industrial Fuel Oil
An oil known to the trade as a light fuel
oil for use in burners where a low vis-
cosity industrial fuel oil is required.
144,500
150 F. See
Note*
1.0%
See
Note-
Saybolt
Universal
at 100 F
125 seconds
No. 5
Industrial Fuel Oil
Same as Federal Specifications Board
specification for bunker oil "B" for
burners adapted to the use of indus-
trial fuel oil of medium viscosity.
146,000
150 F
1.0%
Saybolt
Furol
at 122 F
100 seconds
No. 6
Industrial Fuel Oil
Same as Federal Specifications Board
specification for bunker oil "C" for
burners adapted to oil of high viscosity.
150,000
150 F
.Water
sediment
1.75%
0.25%
Saybolt
Furol
at 122 F
300 seconds
°Adapted from "Fuel Oils," p. 2, U, S. Department of Commerce, Bureau of Standards, Commercial
Standard CS1Z-SS, Washington, 1933.
^Government specifications do not give Btu per gallon, but they are noted here for information only.
'Lower or higher pour points may be specified whenever required by conditions of storage and use.
However, these specifications shall not require a pour point less than 0 F under any conditions.
^Whenever required, as for example in burners with automatic ignition, a maximum flash point may
be specified. However, these specifications shall not require a flash point less than 250 F under any
conditions.
'Pour point may be specified whenever required by conditions of storage and use. However, these
specifications shall n6t require a pour point less than 15 F under any conditions.
452
CHAPTER 27 — FUELS AND COMBUSTION
gallon increases more rapidly than the decrease in heat units per pound,
and oil is bought by the gallon. As a consequence, while a No. 1 oil may
contain 139,000 Btu per gallon, oil No. 5 may test 146,000 Btu per gallon,
or 6 per cent more. Usually there is a differential of 3 i to 4^ between the
No. 1 and No. 5 oils, so that the economy of buying the heavier fuels is
apparent; there remains the economic utilization of the heat content of
the heavier oils.
The cost of oil fuel is dependent also upon the amount that can be
delivered at one time, and the method of delivery. Common practice has
split the tank of the truck delivering oils for domestic use into compart-
ments of 150 to 500-gal capacity, and these unit dumps are made the basis
of price. Where a truck can be connected to a storage-tank fill and
quickly discharge its oil by pump, the price obviously can be less than
where a smaller quantity must be drawn off in 5-gal cans and poured.
For similar reasons an installation that can be supplied from a tank car
on a siding provides for a lower unit fuel cost than one where the oil
must be trucked, even in the large trucks holding 2,000 gal or more that
are used for distributing the heavier oils.
GAS
Gas is broadly classified as being either natural or manufactured.
Natural gas is a mechanical mixture of several combustible and inert
gases rather than a chemical compound. Manufactured gas as dis-
tributed is usually a combination of certain proportions of gases produced
by two or more processes, and is often designated as city gas.
When gas is burned a large amount of water vapor is produced as one
of the products of combustion. This ordinarily escapes up the chimney,
carrying away with it a certain amount of heat. However, when the heat
value of gas is determined in an ordinary calorimeter, this water vapor
is condensed and the latent heat of vaporization that is given up during
the condensation is reported as a portion of the heat value of the gas.
The heat value so determined is termed the gross or higher heat value and
this is what is ordinarily meant when the heat value of gas is specified.
The heat that is reclaimed by the condensation of the water vapor
amounts to about 10 per cent of the total heat value. It is impractical
to utilize the entire higher heat value of the gas in any house^heating
appliance, because to do so it would be necessary to cool the products of
combustion down below their dew point, which is ordinarily in the
neighborhood of 130 F.
Natural gas is the richest of the gases and contains from 80 to 95
per cent methane, with small percentages of the other combustible
hydrocarbons. In addition, it contains from 0.5 to 5.0 per cent of COz,
and from 1 to 12 or 14 per cent of nitrogen. The heat value varies from
700 to 1,500 Btu per cubic foot, the majority of natural gases averaging
about 1,000 Btu per cubic foot. Table 4 shows typical values for the
three main oil fields, although values from any one field vary materially.
Table 4 also gives the calorific values of the more common types of
manufactured gas. Most states have legislation which control^ the distri-
bution of gas and fixes a minimum limit to its heat content. The gross
453
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
or higher calorific value usually ranges between 520 and 545 Btu per cubic
foot, with an average of 535. A given heat value may be maintained and
yet leave considerable latitude in the composition of the gas so that as
distributed the composition is not necessarily the same in different dis-
tricts, nor at successive times in the same district. There are limits to the
variation allowable, because the specific gravity of the gas depends on its
TABLE 4. REPRESENTATIVE PROPERTIES OF GASEOUS FUELS,
BASED ON GAS AT 60 F AND 30 IN. HG.
GAS
BTU PER Cu FT
SPECIFIC
GRAVITY,
AIR =
1.00
Am REQUIRED
FOR COMBUS-
TION,
(Cu FT)
PRODUCTS OP COMBUSTION
THEORETICAL
FLAME TEM-
PERATURE,
(DEG FAHR)
High
(Gross)
Low
(Net)
Cubic Feet
ULTI-
MATE
CO*
Dry
Basis
CQt
#20
Total
with
N*
Natural gas —
Mid-Conti-
nental
967
873
0.57
9.17
0.97
1.92
10.2
11.7
3580
Natural gas —
Ohio
1130
1025
0.65
10.70
1.17
2.16
11.8
12.1
3600
Natural gas —
Pennsylvania
1232
1120
0.71
11.70
1.30
2.29
12.9
12.3
3620
Retort coal gas
575
510
0.42
5.00
0.50
1.21
5.7
11.2
3665
Coke oven gas
588
521
0.42
5.19
0.51
1.25
5.9
11.0
3660
Carburet ted
water gas
536
496
0.65
4.37
0.74
0.75
5.0
17.2
3815
Blue water gas
308
281
0.53
2.26
0.46
0.51
2.8
22.3
3800
Anthracite pro-
ducer gas
134
124
0.85
1.05
0.33
0.19
1.9
19.0
3000
Bituminous
producer gas
150
140
0.86
1.24
0.35
0.19
2.0
19.0
3160
Oil gas
575
510
0.35
4.91
0.47
1.21
5.6
10.7
3725
composition, and too great a change in the specific gravity necessitates a
change in the adjustment of the burners of small appliances.
Table 4 shows that a large proportion of the products of combustion
when gas is burned may consist of water vapor, and that the greater the
proportion of water vapor, the lower the maximum attainable CO* by gas
analysis. The table also shows that a low calorific value does not neces-
sarily mean a low flame temperature since, for example, natural gas has a
theoretical flame temperature of 3600 F and blue water gas of 3800 F,
although it has a calorific value less than one third that of natural gas.
The quantity of air given in Table 4 is that required for theoretical
combustion, but with a properly designed and installed burner the excess
air, can be kept low. The division of the air into primary and secondary-
is a matter of burner design and the pressure of gas available, and also of
the type of flame desired.
' CHAPTER 27 — FUELS AND COMBUSTION
PROBLEMS IN PRACTICE
1 • Name several important properties of coal from a utilization standpoint.
a. Caking tendency, whether none, weak, or strong.
b. Quantity of volatile matter.
c. Friability.
d. Fusibility of the ash.
2 • What are the main data commonly available that fix the qualities of coal,
and do these tell the whole story?
a. Calorific value, Btu per pound.
b. Proximate analysis giving percentages of moisture, volatile matter, fixed carbon, ash,
and sulphur.
c. Temperature at which the ash softens.
d. Screen sizes.
Other important qualities not usually given are the friability of the coal, its caking
tendency, and the qualities of the volatile matter. The percentage of ash and its fusion
temperature do not tell how the ash is distributed or how much of it is less fusible lumps
of slate or shale.
3 • Are there available complete and sufficient data on gas and oils to fix their
burning properties and furnace requirements?
Yes. Because gas and oils are of simple and uniform composition, data are available to
fix their burning properties and furnace requirements, but the ability to control their
combustion is somewhat less determinable.
4 • What effect does moisture in fuels have on then* efficiency?
With any solid fuel, latent and sensible heat are lost at the stack when moisture is dried
out of the fuel in burning, and when its hydrogen is burned. Therefore, such fuels as
sub-bituminous coal and lignite, which are high in moisture content, have a low efficiency.
However, these efficiencies may be improved if the stack gases are cooled to room tem-
perature, by heating the feed water, for example.
5 • What are the advantages of a sized fuel for heating furnaces?
Because a sized fuel encourages a more uniform flow of air through the bed, the burning
will be more uniform, and the bed will be less liable to develop holes and will require less
attention. Uniformity of fuel size is more desirable as the area of the bed becomes
smaller; it is less important with fuels that cake, but with sized fuels the caking will be
more uniform and the air flow through the bed will be steadier. In addition, ash and
pieces of slate are less likely to be segregated and to form lumps of clinker.
6 • Does the size of a fuel affect the quantity of air required to burn it at a
given rate?
The total air required to give the same gas analysis at the stack is independent of the
size of the fuel burned, but for non-caking fuels the ratio of the air passing through the
fuel bed to the total air entering the burner base decreases, for the same thickness of bed,
as the size of the fuel becomes smaller; this decrease is very rapid for sizes less than one
inch. For coals that cake, this ratio will depend on the way the caked bed is broken up
and on the size of the resulting pieces.
7 • Is the volatile matter which is given off when coals are burned of the same
nature in all coals?
No. The products given off by coals when they are heated differ materially in the ratios
by weight of the gases to the oils and tars. No heavy oils or tars are given off by anthra-
cite, and very small quantities are given off by semi-anthracite. As the volatile matter
in the coal increases to as much as 40 per cent of ash-free and moisture-free coal, in-
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
creasing amounts of oils and tars are given up. For coals of higher volatile content, the
relative quantity of oils and tars decreases, so it is low in the sub-bituminous coals and
in lignite.
8 • Is smoke a primary product in the burning of fuels?
Visible smoke may include very small particles of carbon, oil, tar, water (condensed
steam), and ash. Of these, the oils, tars, and ash are mainly primary products, and the
water is partly primary. The carbon, which usually comprises the greater part of the
smoke, results from the breaking up by heat of oils, tars, and such gases as methane, so
it may be considered a secondary product.
9 • Is the sulphur in coals detrimental to combustion?
Not so far as is known, but its complete combustion gives only 25 per cent as much heat
as is given by the same weight of carbon. Sulphur is undesirable because it causes cor-
rosion of flues and stacks, and also because its gases pollute the atmosphere, and damage
buildings and vegetation.
10 • Can any one fuel be said to be the best'fuel?
The term best can be applied to a fuel only after consideration of the cost factor of the
fuel and the equipment necessary for its use. Gas seems to be the most convenient fuel
because of its uniformity, and the ease with which it may be controlled and its burning
made fully automatic.
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Chapter 28
AUTOMATIC FUEL BURNING
EQUIPMENT
Stokers, Residential Stokers, Apartment House Stokers, Com-
mercial Stokers, Domestic Oil Burners, Commercial Oil Burners,
Gas-Fired Appliances, Gas Boilers, Warm Air Furnaces, Space
Heaters, Conversion Burners, Gas Appliances
A UTOMATIC, mechanical equipment for the efficient combustion
-Z~jL of coal, oil, and gas is considered in this chapter.
MECHANICAL STOKERS
Assuming the same intelligence in handling the fire, coal can be burned
more efficiently on a mechanical stoker than on any kind of hand-fired
grate. This does not necessarily mean that a stoker installation may be
more economical, because the amount of coal burned may be so small or the
cost of the installation so high that the savings with stokers may .not be
sufficient to pay for the investment. The operation of burning coal in-
volves uniformity in stoking, proper distribution over the fuel bed,
admission of air as required to all parts of the fuel bed, and disposal of the
ash. The handling of the volatile gas is largely a matter of furnace design
but since this gas forms a considerable portion of the heating value of the
coal, it may also be said that the proper handling of this gas is a function
of firing. All mechanical stokers must provide means of taking care of
these several functions in order fully to serve their purpose.
Stokers may be divided into four types according to their construction
and operation, namely, (1) overfeed flat grate, (2) overfeed inclined grate,
(3) underfeed side cleaning type, and (4) underfeed rear cleaning type.
They may also be classified according to their uses. The following
classification has been adopted by the U. S. Department of Commerce:
Class 1. Residential (Capacity less than 100 Ib coal per hour).
Class 2. Apartment houses and small commercial heating jobs (Capacity 100 to 200 Ib
coal per hour).
Class 3. General commerical heating and small high pressure steam plants (Capacity
200 to 300 Ib coal per hour).
Class 4. Large commercial and high pressure steam plants (Capacity over 300 Ib
per hour).
Overfeed Flat Grate Stokers
This type is represented by the various chain grate stokers. These
stokers receive fuel at the front of the grate in a layer of uniform thickness
and move it back horizontally to the rear of the furnace. Air is supplied
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
under the moving grate to carry on combustion at a sufficient rate to com-
plete the burning of the coal near the rear of the furnace. The ash is
carried over the back end of the stoker into an ashpit beneath. This type
of stoker is suitable for small sizes of anthracite or coke breeze and also
for bituminous coals, the clinker forming characteristics of which make it
desirable to burn the fuel without disturbing it. This type of stoker
invariably requires the use of an arch over the front of the stoker to
maintain ignition of the incoming fuel and to maintain the volatile gas at
a temperature suitable for combustion. Frequently, a rear combustion
arch is required to maintain ignition until the fuel is fully consumed.
Overfeed Inclined Crate Stokers
In general the combustion principle is similar to the flat grate stoker,
but this stoker is provided with rocking grates set on an incline to advance
the fuel during combustion. Also this type is provided with an ash plate
where ash is accumulated and from which it is dumped periodically.
This type of stoker is suitable for all types of coking fuels but preferably
for those of low volatile content. Its grate action has the tendency to
keep the fuel bed well broken up thereby allowing for free passage of air.
Because of its agitating effect on the fuel it is not so desirable for badly
clinkering coals. Furthermore, it should usually be provided with a
front arch to care for the volatile gas.
Underfeed Side Cleaning Stokers
In this type, the fuel is fed in at the front of the furnace to one or more
retorts, is advanced away from the retort as combustion progresses, while
finally the ash is disposed of at the sides. This type of stoker is suitable
for all coking coals while in the smaller sizes it is suitable for small sizes of
anthracites. In this type of stoker the fuel is delivered to a retort beneath
the fire and is raised into the fire. During this process the volatile gas is
released, is mixed with air, and passes through the fire where it is burned.
The ash may be continuously discharged as in the small stoker or may b.e
accumulated on a dump plate and periodically discharged. This stoker
requires no arch as it automatically provides for the combustion of the
volatile gas.
Underfeed Rear Cleaning Stokers
This type carries on combustion in much the same manner as the side
cleaning type, but consists of several retorts placed side by side and
filling up the furnace width, while the ash disposal is at the rear. In
principle, its operation is the same as the side cleaning underfeed.
Class 1 Stokers, Residential
A common type of stoker in this class consists of a round retort having
tuyeres at the top where all of the air for combustion is admitted. Coal
is fed from a storage hopper outside of the boiler by means of a worm into
the bottom of this retort and beneath the fire. The equipment includes a
blower which is, driven by the same motor that drives the stoker.
Some domestic stokers are provided with automatic grate shaking
.mechanism together with screw conveyers for removing the ash frorn> the
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CHAPTER 28 — AUTOMATIC FUEL BURNING EQUIPMENT
ashpit and depositing it in an ash receptacle outside the boiler. Certain
types can also be provided with a coal conveyer which takes coal from the
storage bin and maintains a full hopper at the stoker. They may feed
coal to the furnace either intermittently or with a continuous flow regu-
lated automatically to suit conditions. Where the boiler is provided with
indirect coils for heating the domestic hot water, the stoker may be so
arranged that it can be used the entire year to maintain a continuous hot
water supply.
Class 2 Stokers, Apartment House
This class is used extensively for heating plants in apartments and
hotels, and also for small industrial plants such as laundries, bakeries, and
creameries. The various stokers in this class differ materially in their
design, although the majority are of the underfeed type. The principal
exception is an overfeed type having step action grates in a horizontal
plane and so arranged that they are alternately moving and stationary,
and are designed to advance the fuel during combustion to an ash plate
at the rear.
All of the stokers are provided with a coal hopper outside of the boiler.
In the underfeed types, the coal feed from this hopper to the furnace may
be accomplished by a continuously revolving worm or by an intermittent
plunger. The drive for the coal feed may be an electric motor, or a steam
or hydraulic cylinder. With an electric motor, the connection between
the driver and the coal feed may be through a variable speed gear train
which provides two or more speeds for the coal feed ; or it may be through
a simple gear train and a variable speed driver for the change in speed of
the coal feed ; or a simple gear train with a coal feed having an adjustment
for varying the travel of the feeding device. With a steam or hydraulic
cylinder, the power piston is connected directly to the coal feeding
plunger.
. The stokers in this class vary also in their retort design. It is customary
in the worm-feed type to use a short retort in order that the unsupported
length of worm within the retort may not be too weak for continuous
service. In this type the retort is placed approximately in the middle of
the furnace and is provided with tuyere openings at the top on all sides.
In the plunger-feed type the retort extends from the inside of the front
wall entirely to the rear wall or to within a short distance of the rear wall.
This type of retort has tuyeres on the sides and at the rear.
This class of stokers also differs in the grate surface surrounding the
retort. In many of the worm-feed stokers this grate is entirely a dead
plate on which the fuel rests while combustion is completed. In the dead-
plate type, all of the air for combustion is furnished by the tuyeres at the
retort. Because of this, combustion is well advanced over the retort so
that it may easily be completed by the air which percolates through the
fuel bed. With the dead-plate type of grate the ash is removed through
the fire doors and it is therefore desirable that the fuel used shall be one
in which the ash is readily reduced to a clinker at the furnace temperature,
in order that it may be removed with the least disturbance of the fuel bed.
, In other stokers in this class, the grates outside ,of the retort are air-
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
admitting and shaking grates. These grates permit a large part of the ash
to be shaken into the ash pit beneath, while the clinkers are removed
through the fire doors. With this type of grate, the main air chamber
extends only under the retort while the side grates receive air by natural
draft from the ash pit.
In still other stokers of this class, the main air chamber extends beyond
the retort and is covered with fuel-bearing, air-supplying grates. With
this type of grate, the fuel is supplied with air from the main air chamber
throughout combustion. Also with this type of grate, dump plates are
provided beyond the grates where the ash accumulates and from which it
can be dropped periodically into the ash pit beneath.
Stokers in this class are compactly built in order that they may fit into
standard heating boilers and still leave room for sufficient combustion
space above the grates. The height of the grate is approximately the same
as that of the ordinary grates of boilers, so that it is usually possible to
install such stokers with but minor changes in the existing equipment.
In some districts, there are statutory regulations governing such settings.
These stokers vary in furnace dimensions from 30 in. square to approxi-
mately 66 in. square. The capacity of the stokers is measured by the
amount of coal that can be burned per hour. In general, manufacturers
recommend that, for continuous operation, the coal burning rate shall not
exceed 25 Ib of coal per square foot of grate per hour, while for short
peaks this rate may be increased to 30 Ib per hour. Although these
stokers were designed to burn bituminous coal, they can also be used to
burn the small sizes of anthracite but at a somewhat lower rate. It is
often customary to have the janitor or some other attendant care for the
boiler as one of his duties. Under these conditions the heating plant does
not receive the same careful attention as it would if a man devoted his
entire attention to the fire. With periodic hand-firing, the boiler is
operated inefficiently much of the time. With a stoker, the boiler is
operated at the rate that the conditions require so long as there is coal in
the hopper. With hand firing, it is customary to use the more expensive
sizes of fuel, while with a stoker the smaller sizes are used at a considerable
saving in the cost per ton. Because the stoker responds promptly to auto-
matic regulation, it is possible to maintain a reasonably constant standard.
Also because the stoker feeds the fuel regularly and in small quantities
without losses due to opening doors, it must of necessity be more efficient
than hand firing. This increase in efficiency depends entirely on cbn-
ditions, with a minimum of about 10 per cent and a maximum of about
25 per cent.
Class 3 Stokers, General Commercial
These stokers are suitable for the heating plants of large schools, hotels,
hospitals, or other large institutions as well as industrial plants. This
class is served both by overfeed stokers and by underfeed stokers. The
overfeed stokers are in general of three types, (1) the chain grate, (2)
the rear cleaning inclined grate, and (3) the center cleaning inclined grate
or V-type.
Stokers of this type are usually operated by natural draft, although in
some cases conditions permit the operation of forced draft under the
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CHAPTER 28 — AUTOMATIC FUEL BURNING EQUIPMENT
grates. With most fuels, it is not advisable to operate overfeed grates at
too high a combustion rate because of the greater difficulty of cleaning and
the higher maintenance, but where the fuel is free burning and has a high
ash' fusion temperature, the combustion rate is not so restricted. The
operation of the chain grates and the rear cleaning type of inclined grates
has already been described.
The V-type stoker is practically obsolete although many are still in
operation. In this stoker, the grates are inclined downward from both
sides of the furnace to a low point at the middle where there is either a
dump plate for periodic disposal of the ash or a rotary ash grate for con-
tinuous discharge of ash. In this stoker, the fuel is fed into a hopper at the
top of the grate on each side of the furnace and advanced down the grates
to the center where the refuse is accumulated. This stoker is always
provided with a combustion arch over the entire furnace for the purpose
of assuring thorough combustion of the solid fuel and providing a furnace
temperature sufficiently high to burn the volatile gases. Because of this
high furnace temperature and because so little of the boiler surface is
exposed to the fire to assist in carrying off the heat by radiation, this
stoker is characterized by severe clinkering in the ash area. With all
types of overfeed stokers, the most desirable installations are in boilers
which are operated with comparatively uniform loads and moderate rates
of combustion, since, even with good combustion arches, fluctuating loads
or high combustion rates result in free volatile gas and this in turn means
smoke.
The underfeed stokers in this class were the first of the type to be
developed as at the time of their development very few large boilers were
in use. The stokers are not so varied in design as those in the smaller
class although in principle they are much the same. Practically all of
them are of the plunger coal feed type with retorts extending the entire
length of the furnace, with air supplying grates adjacent to the retorts,
and with manually-operated dump plates at the sides of the furnace.
The coal feeding plunger is operated by a steam or electric driver through
a reduction gearing, or by a steam or hydraulic piston connected directly
to the coal feeding plimger.
These stokers are heavily built and designed to operate continuously at
'high boiler ratings with a minimum amount of attention. Because of the
fact that all volatile gas must pass through the fire before reaching the
combustion chamber, these stokers will operate smokelessly under
ordinary conditions. Also because of the fact that these stokers are
always provided with forced draft, they are the most desirable type for
fluctuating loads or high boiler ratings.
In the design of the grates for supporting the fuel between the retort
and the ash plates, the stokers differ in providing for movement of the
fuel during, combustion. Some stokers are designed with fixed grates of
sufficient angle to provide for this movement as the bed is agitated by the
incoming fuel, while others have alternate moving and stationary bars in
this area and provide for this movement mechanically. In either type,
with proper operation, all refuse will be deposited at the dump plate.
Another difference in these stokers is that some makes use a single air
chamber under the whole grate area thus having the same air pressure
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
tinder the ignition area as under the rest of the grate, while others have a
divided air chamber using the full air pressure under the ignition area and
a reduced air pressure under the remainder of the grate. These stokers
vary in size from approximately 5 ft square to a maximum of 8 J^ ft square.
Class 4 Stokers, Large Commercial
These stokers are usually of the underfeed type with multiple retorts
and either side cleaning or rear cleaning. In the side cleaning type there
may be as many as three retorts in the furnace, and the stoker functions
in the same manner as has been described for the single retort. These
stokers ^are usually limited in length to approximately 8J^ ft while the
width may be as great as 10}^ ft. In the rear cleaning stokers the number
of retorts and the dimensions of the furnace are practically unlimited.
DOMESTIC OIL BURNERS
The number of combinations of the characteristic elements of domestic
oil burners is rather large and accounts for the variety of burners found in
actual practice. Domestic oil burners may be classified as follows:
1. AIR SUPPLY FOR COMBUSTION
a. Atmospheric — by natural chimney draft.
b. Mechanical — electric-motor-driven fan or blower.
c. Combination of (a} and (b) — primary air supply by fan or blower and secondary
air supply by natural chimney draft.
2. METHOD OF OIL PREPARATION
a. Vaporizing — oil distills on hot surface or m hot cracking chamber.
b. Atomizing — oil broken up into minute globules.
(1) Centrifugal — by means of rotating cup or disc.
(2) Pressure — by means of forcing oil under pressure through a small
nozzle or orifice.
(3) Air or steam — by high velocity air or steam jet in a special type of
nozzle.
(4) Combination air and pressure — by air entrained with oil under pressure
and forced through a nozzle.
c. Combination of (a) and (b).
3. TYPE OF FLAME
a. Luminous — a relatively bright flame. An orange-colored flame is usually best
if no smoke is present.
b. Non-luminous — Bunsen-type flame (i.e., blue flame).
4. METHODS OF IGNITION
a. Electric,
(1) Spark — by transformer producing high-voltage sparks. Usually
shielded to avoid radio interference. May take place continuously
while the burner is operating or just at the beginning of operation.
(2) Resistance — by means of hot wires or plates.
b. Gas.
(1) Continuous — pilot light of constant size.
(2) Expanding — size of pilot light expanded temporarily at the beginning
of burner operation.
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CHAPTER 28 — AUTOMATIC FUEL BURNING EQUIPMENT
c. Combination — electric sparks light the gas and the gas flame ignites the oil.
d. Manual — by manually-operated gas torch for continuously operating burners.
5. MANNER OF OPERATION
a. On and off — burner operates only a portion of the time (intermittent).
b. High and low — burner operates continuously but varies from a high to a low
flame.
c. Graduated — burner operates continuously but flame is graduated according to
needs by regulating both air and oil supply.
Air and Oil Supply
The object of regulating the air and oil supplies is to obtain a complete
mixture of the proper quantities of oil and air so the fire will be clean and
efficient. Proper and dependable ignition also depends upon the ability
of the burner to produce consistent fuel-air mixtures. The type and shape
of flame depend largely upon the methods of air and oil supply employed.
It should be pointed out that this mixture burns in a space called the
furnace, which is lined with refractory bricks or other heat-resistant
substances for the purpose of maintaining that space at a high tempera-
ture so that the oil and air may completely unite and burn. Excessive
cooling before combustion is completed stops the combustion process and
causes soot. The furnace is in some instances a valuable auxiliary in
assisting in the actual mixture of oil and air and in modifying the flame
shape, besides its primary function of maintaining high temperatures.
The size and shape of furnace required are important, especially where the
dimensions of the space into which the burner is to be placed are already
fixed.
Atornization
The purpose of atomization is greatly to increase the surface area of a
given quantity of oil in order to accelerate the change from the liquid
state (in which oil cannot burn) to the gaseous or vaporous state, in which
state it is one of the elementary fuels, gaseous hydrocarbon. This con-
version is largely accomplished through the action of radiant heat energy
upon the flying globules of oil, and the tremendously increased surface
provided aids gasification.
Air for Combustion
Air for combustion usually is supplied by a motor-driven fan, several
types being in common use. Electric motors varying from Ko hp to H hp
ar,e used and are started and stopped by the control mechanism. In most
cases, they are direct-coupled to the fan as well as to a gear or lobe pump
for drawing the oil from the storage tank, and in some cases, to a pump
for forcing the oil through the nozzle.
All of the air required for combustion can be supplied by the blower, or
else only the primary air can be supplied under pressure and provision
rnadle so that the remainder will be drawn into the combustion chamber
by the natural draft developed by the chimney or by an injector-like
action of the primary air. In any event there should be definite control
Of the' quantity of "air as well as of the rate of oil supply. Some method of
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
draft regulation is advisable in order to secure proper air regulation. It is
necessary to supply more air than is actually required for complete com-
bustion of the oil, but the amount of excess air should be reduced to the
lowest workable minimum. Laboratory tests frequently show 25 per cent
to 50 per cent more air than is required for combustion, yet field tests
indicate that the average burner operates with from 50 per cent to 125
per cent excess air, with a corresponding reduction in the efficiency of the
burner. Many domestic burners are extremes of simplicity, the only mov-
ing parts being the motor armature with a shaft and direct-connected
fan and pump set.
Type of Flame, Ignition
If the vaporizing of the atomized oil and the combustion are concurrent
events, a luminous flame will usually result. If vaporization and mixing
are accomplished before combustion, a non-luminous flame will result.
Some burners may produce either type of flame according to the adjust-
ment made.
A limited comparison of these two types of flame shows no inherent
superiority of one over the other so far as thermal efficiencies are concerned.
This is definitely true when the burners are placed in boilers having ample
indirect surface, and is probably true in general. The moot question pf
radiation has not been conclusively settled. There are indications that
the radiation of luminous and non-luminous flames in boiler furnaces are
practically the same. More information is needed upon this subject.
It is true, however, that a non-luminous flame may show low excess air
and the presence of carbon monoxide, but no smoke. Low excess air
with a luminous flame will usually show little or no carbon monoxide, but
will be unmistakably smoky. Visual indications, especially with a blue
flame, may therefore be quite unreliable.
When a burner is operating intermittently under the control of a
thermostat, some positive form of ignition is required to function every
time there is a call for heat.
The necessity for certain ignition under adverse conditions, when the
line voltage is low or the oil is cold is paramount, and this phase of burner
design and operation has been given the closest attention, as faulty igni-
tion is more to be feared than improper operation once the flame is
established.
The effect of the air and oil setting is important, since it may be neces-
sary in some instances to adjust for greater excess air than is otherwise
required in order to get a mixture suitable for certainty of ignition.
Recent research1 at Yale University, conducted in cooperation with the
A.S.H.V.E. Research Laboratory and the American Oil Burner Associa-
tion, reveals that the various methods of operation (i.e., on and off, high
and low, and graduated) all have potential advantages and disadvantages
and that a choice in any case requires a consideration of the heat-absorbing
characteristics of the boiler in which the burner is to operate. From the
standpoint of efficiency of operation it seems that there is little choice if
^Intermittent Operation of Oil Burners, by L. E. Seeley and J. H. Powers (A.S.H.V.E. TRANSACTIONS,
Vol. 38, 1932).
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CHAPTER 28 — AUTOMATIC FUEL BURNING EQUIPMENT
at the maximum setting of all burners the boiler efficiency were at its
maximum value. If, on the other hand, the boiler were operating beyond
its point of maximum efficiency, then it appears that the graduated type
might show better results. The following additional factors should be
considered :
1. The intermittent type should be set at its point of most efficient combustion.
2. An intermittent burner should be set for a higher total heat output than either of
the other two types in order to get the acceleration necessary when heat is required.
This may in some cases give less economical performance due to the increased boiler load.
3. An interruption in electric current might in some instances be troublesome with
continuously operating burners where manual ignition is employed.
4. The continuously operating burners must have a minimum fuel setting low enough
to prevent overheating in mild weather or during the summer if the boiler is used for
domestic hot water.
5. Electrical operating costs must be considered, but must be based upon known
power requirements. The power requirements of some burners will be several times as
nigh as others, so any generalization on operating costs is futile.
6. Evenness of heat supply will have some influence on uniformity of temperature.
7. Number and cost of controls which reflect in the manufacturing costs.
This entire subject, therefore, is likely to be somewhat perplexing
because of the necessity of knowing, and the difficulty in determining,
the efficiency characteristics of many heating boilers. Selections of oil
burners on the basis of their manner of operation will probably be largely
a matter of preference. The advent of special boilers for oil burning will
provide the engineer with the opportunity for greater discrimination.
Temperature Control, Protective Devices
Domestic oil burners are controlled directly from the change in tem-
perature of a designated control room (usually the living room, dining
room or hall), and by temperature or pressure variations in the boiler.
Oil-burner installations put in only a few years ago were simplified to
the extent of having a single control element — the room thermostat —
that started and stopped the burner. The modern installation provides,
in addition, electrical devices inter- wired with the control system to in-
sure against poor operation and to guard against troubles brought on
by the characteristics of the heating plant.
One control system provides an instrument actuated by two tempera-
ture bulbs, one placed in the outdoor air and the other in a designated
part of the heating system. The control is actuated by both bulbs and is
designed to maintain the heating medium at a temperature to suit the
variations in outdoor temperature, the lower the outdoor temperature the
higher the temperature of the heating medium. Other devices have been
developed to maintain a certain minimum temperature that will effectively
prevent the downward window currents of cold air from reaching and
traveling across the floor, regardless of the room thermostat.
Owing to the comparative intensity of heat production with a burner,
a boiler with limited water storage above the crown sheet might pass
steam to the radiator system so rapidly, at starting, that the sheet would
be uncovered, with probable damage to the boiler structure. A low-water
safety can be so wired into the system that the burner will be stopped
before the water level is reduced to the danger point, or a boiler feed can
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
be installed to add water to the boiler to maintain a safe level, instead
of stopping the burner. Either or both should form part of a first-class
installation.
Again, with either steam or water systems, the burner control can be
inter-wired with a thermostatic device having its temperature Clement
introduced into the boiler near the top, its function being to limit the
maximum temperature of water or pressure of steam so the burner will
be shut off before dangerous temperatures or pressures are reached. Win-
dows of the room in which the thermostat is located are sometimes opened
to air out the house in the morning, and if they are not closed promptly,
the burner will operate continuously and possibly develop temperature
and pressure conditions that might be detrimental to the boiler. This is
where the safety device can be used to offset the carelessness of the
human being.
Safety controls have been developed for intermittent burners to guard
against failure of ignition and in some instances against momentary flame
failures. In general, regulatory devices are well developed and depend-
able. Otherwise the domestic oil burner probably would not have been
possible.
For further information on temperature control with oil burners, see
Chapter 14.
Boilers for Domestic Oil Burners2
Boilers used with domestic installations may be those designed for solid
fuel or those designed for liquid fuel. The latter are coming to the fore
with great rapidity as they usually have greatly increased secondary sur-
face. Many are of copper or steel tube design. Increased efficiencies of
5 to 15 per cent are often obtainable with boilers designed especially for
liquid fuel.
It is possible to go to extremes in providing secondary surfaces sufficient
to reduce flue temperatures to the order of 250 F to 300 F, with the result
that the added resistance through the flues may necessitate the use of a
booster fan to insure sufficient draft. It is difficult to obtain satisfactory
efficiencies with boilers having little or no secondary surfaces, where the
hot products of combustion pass almost immediately from the combustion
chamber to the flue; in fact a high efficiency is unlikely with any fuel
under such conditions, and the intermittent burner is especially at a
disadvantage because of its characteristic development of heat at a high
rate while it is operating.
It is essential that the flame produced by an oil burner, especially where
it is strongly luminous, be kept from contact with the water-backed sur-
faces of the combustion chamber, and to this end bricking or its equivalent
must be provided in most cases. Where a burner fires through the ash pit,
doorframe bricking must protect the unbacked surfaces of the ash pit.
The same fire bricking constitutes the actual combustion chamber for the
burner flame, and materially increases the combustion volume for a given
boiler.
*For additional information on this subject, refer to Study of Performance Characteristics of Oil Burners
and Low-Pressure Heating Boilers, by L. E. Seeley and E, J. Tavanlar (A.S.H.V.E. TRANSACTIONS, Vol. 37,
1931).
466
CHAPTER 28 — AUTOMATIC FUEL BURNING EQUIPMENT
Installation
The intelligence and care with which a burner is installed largely deter-
mine the satisfaction that will result from its operation. Two plans for the
installation of burners are in general use. In the first, the dealer makes
all installations. In the other, sales agencies function only to make sales,
and the installation for as many as twenty such sales offices is done by a
centrally located installation force, usually factory controlled.
Some burners are adjusted for oil rate by means of a blind needle valve
that can be operated only with a special wrench ; others, by changing the
size of the orifice; others, by a combination of orifice size and pressure.
In any event, changes in the firing rate, involving careful air and draft
adjustment to match the oil rate, should be made by only a trained man,
to.
5- IOOD-
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Assumptions
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iler Worse power
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- 240 B.tu. per Uour
.Ft. Wot water Radia
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e efficiency on J
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34567, .-
Oil Consumption, Gals, per Hour
FIG. 1. FULL LOAD RATE OF OIL CONSUMPTION FOR HEATING BOILERS
preferably with the aid of an Orsat test set so that the degree of combus-
tion efficiency can be determined. It is practically impossible to set a
burner flame by eye, although that has been general practice in the past.
The industry is turning to the Orsat and, as a result, more domestic
burners are operating at from 9 to 12 per cent C02, representing a higher
efficiency combustion than at 5 to 8 per cent, as frequently is the case
where the burner is adjusted by eye.
Air for Combustion
It is essential that the basement, or at least that portion^ used ^as a
boiler room, be open to the outside air, in order that sufficient air be
available for combustion. Frequently a case of poor operation will be
found where a test with a draft gage made by inserting the tube through
the keyhole of the outer door will show that there is a partial vacuum in
the basement when the burner is running, all of the combustion air coming
467
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
through the keyhole and minute cracks. A simple remedy is to cut an
inch from the bottom of the outer door.
In order to achieve satisfactory heating at the lowest cost, careful con-
sideration should be given to oil, air and draft adjustment. The oil
adjustment should be determined from the total heat requirements to be
met. The heat loss of the building plus an allowance for piping plus
20 to 25 per cent for pick-up establishes the maximum output required
from the boiler. Fig. 1 indicates the oil required in gallons. ^ Piping
allowances will usually vary between 25 and 10 per cent, decreasing with
an increase in the size of the building.
With the oil rate thus fixed, the air and draft should be set to give
efficient combustion (that is, 10 to 12 per cent C02). The furnace draft
should be set reasonably low and should be maintained constant by
means of an automatic draft regulator. Without this the air supply will
fluctuate, causing uneven performance. A check should be made to
insure that ignition will be satisfactory under all conditions. An oil burner
of the continuous type might dispense with all or part of the pick-up
allowance due to the nature of its operation. Careful adjustment will
provide ample heat output under all conditions, will minimize the load on
the boiler, and will establish the most favorable conditions for intermit-
tent operation.
An essential element in the satisfactory operation of domestic oil burners
is the provision for maintenance and service for the burners. What might
be called emergency service for mechanical or electrical failure of the burner
has rapidly diminished during the last few years until a level has been
reached where groups of 100 to 1000 burners in a community consistently
will require an average of not more than one call per burner per heating
season. Maintenance service is coming into general practice where, for a
fixed annual payment, regular inspection is made of the burner, and faulty
operation corrected before the burner becomes inoperative. This service
may contemplate entire overhauling of the burner during the summer,
and may include annual cleaning of the boiler flues with a specially de-
signed vacuum cleaner.
Domestic Hot Water Supply
Provision may be made for heating domestic water through exchange
heaters attached to the boiler, in which water is maintained at a fixed
temperature or steam at a set pressure during the entire year. The flow
of water or steam to the radiators is controlled by electrically-operated
valves, which remain closed during warm weather and open (through the
functioning of the room thermostat) when heat is required in the house.
The room thermostat either causes heat to be produced by starting the
burner when the room temperature drops to a predetermined point, or
closes the circuit of the motor by operating a valve in the flow line of the
heating system, the motor opening the water or steam valve and per-
mitting water or steam immediately to flow to the radiators. When the
flow in a water heating system is sluggish, the room thermostat also can
start the motor of a circulation pump, thereby decreasing the time re-
quired to bring the room temperature up to the desired point.
It is usual in small steam heating systems to dispense with the motor-
468
CHAPTER 28 — AUTOMATIC FUEL BURNING EQUIPMENT
operated valve and by means of an aquastat maintain the boiler water at
a constant temperature but well below the steaming temperature (i.e.,
140 to 180 F). The lowest temperature setting that will produce suf-
ficiently hot water will be the most economical. The aquastat will
always function in such a way as to maintain this temperature except
when the room thermostat calls for heat, which means that a call for
steam can be more quickly obtained.
Another type of control valve available for hot water systems is
thermostatically operated so as to prevent a flow of water to the heating
system until the call of the room thermostat for heat raises the water
temperature above that normally required for domestic hot water. It
should be noted that, except in the case of the graduated burner, the
water temperature in the heating system will nearly always reach its
maximum, thereby depriving this system to some degree of its natural
advantage of modulation.
COMMERCIAL OIL BURNERS
Liquid fuels are used for heating apartment buildings, hotels, public
and office buildings, schools, churches, hospitals, department stores, as
well as industrial plants of all kinds. Contrary to domestic heating, con-
venience seldom is a dominating factor, the actual net cost of heat pro-
duction usually controlling the selection of fuel. Some of the largest office
buildings have been using oil for many years. Many department stores
have found that floor space in basements and sub-basements can be used
to better advantage for merchandising wares, and credit the heat pro-
ducing department with this saving.
Wherever possible, the boiler plant should be so arranged that either
oil or solid fuel can be used at will, permitting the management to take
advantage of changes in fuel costs if any occur. Each case should be
considered solely in the light of local conditions and prices.
Burners for commercial heating may be either large models of types
used in domestic heating, or special types developed to meet the condi-
tions imposed by the boilers involved. Generally speaking, such burners
are of the mechanical or pressure atomizing types, the former using
rotating cups producing a horizontal torch-like flame. As much as 350 gal
of oil per hour can be burned in these units, and frequently they are
arranged in multiple on the boiler face, from two to five burners to each
boiler.
The larger installations are nearly always started with a hand torch,
and are manually controlled, but the use of automatic control is increasing,
and completely automatic burners are now available to burn the two
heaviest grades of oil. Nearly all of the smaller installations, in schools,
churches, apartment houses and the like, are fully automatic.
Because of the viscosity of the heavier oils, it is customary to heat them
before transferring by truck tank. It also has been common practice to
preheat the oil between the storage tank and the burner, as an aid to
movement of the oil as well as to atomization. This heating is accomplished
by heat-transfer coils, using water or steam from the heating boiler, and
heating the oil to within 30 deg of its flash point.
469
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Unlike the domestic burner, units for large commercial applications
frequently consist of atomizing nozzles or cups mounted on the boiler
front with the necessary air regulators, the pumps for handling the oil
and the blowers for air supply being mounted in sets adjacent to the
boilers. In such cases, one pump set can serve several burner units, and
common prudence dictates the installation of spare or reserve pump sets.
Pre-heaters and other essential auxiliary equipment also should be in-
stalled in duplicate.
Boiler Settings
As the volume of space available for combustion is the determining
factor in oil consumption, it is general practice to remove grates and
extend the combustion chamber downward to include or even exceed the
ash-pit volume; in new installations the boiler should be raised to make
added volume available. Approximately 1 cu ft of combustion volume
should be provided for every developed boiler horsepower, and in this
volume from 1.5 to 2 Ib of oil can properly be burned. This cor-
responds to a maximum liberation of about 38,000 Btu per cubic foot per
hour. There are indications that at times much higher fuel rates may be
satisfactory. This in turn suggests that the value of 38,000 Btu per cubic
foot per hour might be adjusted according to good engineering judgment.
For best results, care should be taken to keep the gas velocity below 40 ft
per second. Where checkerwork of brick is used to provide secondary air,
food practice calls for about 1 sq in. of opening for each pound of oil
red per hour. Such checkerwork is best adapted to flat flames, or to
conical flames that can be spread over the floor of the combustion chamber.
The proper bricking of a large or even medium sized boiler for oil firing is
important and frequently it is advisable to consult an authority on this
subject. The essential in combustion chamber design is to provide
against flame impingement upon either metallic or fire-brick surfaces.
Manufacturers of oil burners usually have available detailed plans for
adapting their burners to various types of boilers, and such information
should be utilized.
GAS-FIRED APPLIANCES
The increased use of gas for house heating purposes has resulted in the
production of such a large number of different types of gas-heating
systems and appliances that today there is probably a greater variety of
them than there is for any other kind of fuel.
Gas-fired heating systems may be classified as follows:
I. Gas-Designed Heating Systems.
A. Central Heating Plants.
1. Steam, hot water, and vapor boilers.
2. Warm air furnaces.
B. Unit Heating Systems.
1. Warm air floor furnaces.
2. Industrial unit heaters.
3. Space heaters.
4. Garage heaters.
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CHAPTER 28 — AUTOMATIC FUEL BURNING EQUIPMENT
II. 'Conversion Heating Systems.
A. Central Heating Plants.
1. Steam, hot water and vapor boilers.
2. Warm air basement furnaces.
The majority of these systems are supplied with either automatic or
manual control. Central heating plants, for example! whether gas
designed or conversion systems, may be equipped with room temperature
control, push button control, or manual control.
Although no exact rules can be prescribed as to the field best covered by
each of the foregoing systems, each installation will have problems point-
ing more or less directly to some particular type of heating equipment.
Gas-Fired Boilers
Information on gas-fired boilers will be found in Chapter 25.
Either snap action or throttling control is available for gas boiler opera-
tion. This is especially advantageous in straight steam systems because
steam pressures can be maintained at desired points, while at the same
time complete cut-off of gas is possible when the thermostat calls for it.
Warm Air Furnaces
There are two general classes of gas-fired warm air furnaces, the
gravity furnace which depends upon the natural tendency of heated air to
rise, providing the proper circulation of heated air into the room, and the
mechanical circulation furnace by which the air to be heated is forced
through or drawn through the furnace by means of a fan.
Warm air furnaces are variously constructed of cast iron, sheet metal
and combinations of the two materials. If sheet metal is used, it must be
of such a character that it will have the maximum resistance to the cor-
rosive effect of the products of combustion. With some varieties of
manufactured gases, this effect is quite pronounced. Warm air furnaces
are obtainable in sizes from those sufficient to heat the largest residence
down to sizes applicable to a single room. The practice of installing a
number of separate furnaces to heat individual rooms is peculiar to mild
climates, such as that of southern California. Small furnaces, frequently
controlled by electrical valves actuated by push-buttons in the room
above, are often installed to heat rooms where heat may be desired for an
hour or so each day. These furnaces are used also for heating groups of
rooms in larger residences. In a system of this type each furnace should
supply a group of rooms in which the heating requirements for each room
in the group are similar as far as the period of heating and temperature
to be maintained are concerned. Bedrooms, living rooms, and dining
rooms often present excellent possibilities for this type of furnace.
The same fundamental principle of design that is followed in the con-
struction of boilers, that is, breaking the hot gas up into fine ^ streams so
that all particles are brought as close as possible to the heating surface,
is equally applicable to the design of warm air furnaces. The desirability
of using an appliance designed for gas, when gas is to be the fuel, applies
even more strongly to furnaces than to boilers.
Codes for proportioning warm air heating plants, such as that formu-
471
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
lated by the National Warm Air Heating Association (see note p. 401),
are equally applicable to gas furnaces and coal furnaces. Recirculation
should' always be practiced with gas-fired warm air furnaces. It not only
aids in heating, but is essential to economy. Where fans are used in
connection with warm air furnaces for residence heating, it is well to
have the control of the fan and of the gas so coordinated that there will
be sufficient delay between the turning on of the gas and the starting of
the fan to prevent blasts of cold air being blown into the heated rooms.
An additional thermostat in the air duct easily may be arranged to
accomplish this.
Floor Furnaces
Warm air floor furnaces are well adapted for heating first floors, or
where heat is required in only one or two rooms. A number may be used
to provide heat for the entire building where all rooms are on the ground
floor, thus giving the heating system flexibility as any number of rooms
may be heated without heating the others. With the usual type the
register is installed in the floor, the heating element and gas piping being
suspended below. Air is taken downward between the two sheets of the
double casing and discharged upward over the heating surfaces and into
the room. The appliance is controlled from the room to be heated by
means of a control lever located near the edge of the register. The handle
of the control is removable as a precaution against accidental turning
on or off of the gas to the furnace.
Space heaters are generally used for auxiliary heating, but may be, and
are in many cases, installed for furnishing heat to entire buildings. Space
heaters are quite extensively used for house heating in milder climates
such as exist in the South and Southwest. With the exception of wall
heaters, they are portable, and can be easily removed and stored during
the summer season. Although they should be connected with solid piping
it is sometimes desirable to connect them with flexible gas tubing in which
case a gas shut-off on the heater is not permitted, and only A.G.A.
approved tubing should be used.
Space Heaters
Parlor furnaces or circulators are usually constructed to resemble a
cabinet radio. They heat the room entirely by convection, i.e., the cold
air of the room is drawn in near the base and passes up inside the jacket
around a drum or heating section, and out of the heater at or near the top.
These heaters cause a continuous circulation of the air in the room during
the time they are in operation. The burner or burners are located in the
base at the bottom of an enclosed combustion chamber. The products of
combustion pass up around baffles within the heating element or drum,
and out the flue at the back near the top. They are well adapted not only
for residence room heating but also for stores and offices.
Radiant heaters make admirable auxiliary heating appliances to be used
during the occasional cool days at the beginning and end of the heating
season when heat is desired in some particular room for an hour or two.
The radiant heater gives off a considerable portion of its heat in the form
of radiant energy emitted by an incandescent refractory that is heated by
472
CHAPTER 28 — AUTOMATIC FUEL BURNING EQUIPMENT
a Bunsen flame. They are made in numerous shapes and designs and in
sizes ranging from two to fourteen or more radiants. Some have sheet-
iron bodies finished in enamel or brass while others have cast-iron or brass
frames with heavy fire clay bodies. An atmospheric burner is supported
near the center of the base, usually by set screws at each end. Others
have a group of small atmospheric burners supported on a manifold
attached to the base. Most radiant heaters are supported on legs and are
portable; however, there are also types which are encased in a jacket
which fits into the wall with a grilled front, similar to the ordinary wall
register. Others are encased in frames which fit into fireplaces.
Gas-fired steam and hot water radiators are popular types of room heating
appliances. They provide a form of heating apparatus for intermittently
heated spaces such as stores, small churches and some types of offices and
apartments. They are made in a large variety of shapes and sizes and are
similar in appearance to the ordinary steam or hot water radiator con-
nected to a basement boiler. A separate combustion chamber is provided
in the base of each radiator and is usually fitted with a one-piece burner.
They may be secured in either the vented or unvented types, and with
steam pressure, thermostatic or room temperature controls.
Warm air radiators are similar in appearance to the steam or hot water
radiators. They are usually constructed of pressed steel or sheet metal
hollow sections. The hot products of combustion circulate through the
sections and are discharged out a flue or into the room, depending upon
whether the radiator is of the vented or unvented type.
Garage heaters are usually similar in construction to the cabinet
circulator space heaters, except that safety screens are provided over all
openings into the combustion chamber to prevent any possibility of
explosion from gasoline fumes or other gases which might be ignited by
an open flame. They are usually provided with automatic room tem-
perature controls and are well suited for heating either residence or
commercial garages.
Conversion Burners
Residence heating with gas through the use of conversion burners in-
stalled in coal-designed boilers and furnaces represents a common type
of gas-fired house heating system, especially in natural gas territories.
In many conversion burners radiants or refractories are employed to
convert some of the energy in the gas to radiant heat. Others are of the
blast type with luminous flames, operating without refractories. In each
case an attempt is made to transfer the majority of the heat from the gas
to the medium to be heated within the fire pot itself because of the low
heat transfer that takes place in the flue passages.
Many conversion units are equipped with sheet metal secondary air
ducts which are inserted through the ash-pit door. The duct is equipped
with automatic air controls which open when the burners are operating
and close when the gas supply is turned off. This prevents a large part
of the circulation of cold air through the combustion space of the ap-
pliance when not in operation. By means of this duct the air necessary
for proper combustion is supplied directly to the burner, thereby making
473
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
it possible to reduce the amount of excess air passing through the com-
bustion chamber.
Conversion units are made in many sizes both round and rectangular
to fit different types and makes of boilers and furnaces. They may be
secured with manual, push button, or room temperature control.
Sizing Gas-Fired Heating Plants
While gas-burning equipment can be and usually is so installed as to be
completely automatic, maintaining the temperature of rooms at a pre-
determined and set figure, there are in use installations which are manually
controlled. Experience has shown that in order to effectively overcome
the starting load and losses in piping,, a manually-controlled gas boiler
should have an output as much as 100 per cent greater than the equivalent
standard cast-iron column radiation which it is expected to serve.
Boilers under thermostatic control, however, are not subject to such
severe pick-up or starting loads. Consequently, it is possible to use a
TABLE 1. SELECTION FACTORS FOR GAS BOILERS
CAST-IRON STEAM RADIATION
(EQUIVALENT SQUARE FEBT)
SELECTION FACTOR
(PER CENT)
500
56.0
800
54.0
1,200
51.0
1,600
48.0
2,000
45.0
3,000
42.5
4,000 and over
40.0
much lower selection, or safety, factor. A gas-fired boiler under ther-
mostatic control is so sensitive to variations in room temperatures that in
most cases a factor of 25 per cent is sufficient for pick-up load.
The factor to be allowed for loss of heat from piping, however, must
vary somewhat, the proportionate amount of piping installed being con-
siderably greater for small installations than for large ones. Consequently,
a selection factor for thermostatically controlled boilers must be variable.
Table 1 gives selection factors to be added to the installed steam radiation
under thermostatic control. They have been established by experience
and are recommended by the American Gas Association.
The same factors may be used in determining the gas demand for which
conversion burners installed in steam or hot water boilers should be set.
Multiplying the equivalent direct heating surface (radiation) by 240 and
adding the appropriate percentage from Table 1, and then dividing by the
heat value of the gas and by the heating efficiency (see discussion of
heating efficiencies in Chapter 29), gives the proper hourly rate of gas
consumption. However, inadequate boiler heating surface for gas
burning, often encountered in coal-designed boilers converted to gas, may
necessitate operation at a lesser demand, resulting in much slower pick-up
and less margin of safety for piping loss.
Appliances used for heating with gas should bear the approval seal1
474
CHAPTER 28 — AUTOMATIC FUEL BURNING EQUIPMENT
of the American Gas Association Testing Laboratory. Installations should
be made in accordance with the recommendations shown in the publica-
tions of that association.
Ratings for Gas Appliances
Since a gas appliance has a heat-generating capacity that can be pre-
dicted accurately to within 1 or 2 per cent, and since this capacity is not
affected by such things as condition of fuel bed and soot accumulation,
makers of these appliances have an opportunity to rate their product in
exact terms. Consequently all makers give their product an hourly Btu
output rating. This is the amount of heat that is available at the outlet of
a boiler in the form of steam or hot water, or at the bonnet of the furnace
in the form of warm air. The output rating is in turn based upon the
Btu input rating which has been approved by the American Gas Asso-
ciation Testing Laboratory and upon an average efficiency which has
been assigned by that association.
In the case of boilers, the rating can be put in terms of square feet of
equivalent direct radiation by dividing it by 240 for steam, and 1503 for
water. This gives what is called the American Gas Association rating, and
is the manner in which all appliances approved by the American Gas
Association Laboratory are rated. To use these ratings it is only necessary
to increase the calculated heat loss or the equivalent direct radiation load
by an appropriate amount for starting and piping, and to select the boiler
or furnace with the proper rating.
The rating given by the American Gas Association Laboratory is not
only a conservative rating when considered from the standpoint of
capacity and efficiency, but is also a safe rating when considered from the
standpoint of physical safety to the owner or caretaker. The rating that
is placed upon an appliance is limited by the amount of gas that can be
burned without the production of harmful amounts of carbon monoxide.
This same limitation applies to all classes of gas-consuming heating
appliances that are tested and approved by the Laboratory. Gas boilers
are available with ratings up to 14,000 sq ft of steam, while furnaces with
ratings up to about 500,000 Btu per hour are available. (See Chapter 23.)
Installation Features
One feature of the piping installation that adds to the satisfactory
service rendered by gas boilers is provision for adequate and rapid venting
of the air from steam heating systems. If air leaks into the steam dis-
tribution system during the period that the gas is turned off, and then
vents out slowly when the thermostat calls for heat, the result will be a
further cooling of the premises between the time that the thermostat
calls for heat and the time that steam reaches the radiators. A freely
venting steam or vapor system gives maximum economy and minimum
temperature variation. When gas boilers are attached to existing heating
plants, it is good practice to check the effectiveness of the venting devices
»A value of 160 for the heat emission of hot water radiators is used by many engineers. The actual heat
emission, however, depends on the temperature of the water and of the surrounding air. See Chapters
30 and 33.
475
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
and if necessary to replace them with more effective ones that will prevent
the return of air into the heating system, and also to check the tightness
of the piping.
Frequently when a coal boiler is already installed in a home, it
is expedient to leave the coal boiler in place, and to cross-connect the
gas boiler with it. Where gas heating is new to the community, it pro-
duces a more secure feeling in the customer's mind when putting in gas-
fired house-heating equipment, if he knows that he can burn coal at any
time he may desire. For steam or vapor installations, it is desirable to
have the water line in both boilers at the same level.
PROBLEMS IN PRACTICE
1 • What functions must an automatic stoker perform in burning coal?
An automatic stoker must distribute the coal evenly over the fuel bed, and fire it uni-
formly. It must introduce air in proper quantities to all parts of the fuel bed, and dispose
of the ash without interfering with the combustion process. Indirectly, the stoker is
responsible for the proper burning of the volatile fuel gases in the combustion space
above the fuel bed.
2 • Classify stokers as to construction and operation.
a. Overfeed flat grate.
b. Overfeed inclined grate.
c. Underfeed side cleaning type.
d. Underfeed rear cleaning type.
3 • What classification may be made of stokers as to their use?
Class 1. For residences (Capacity less than 100 Ib of coal per hour).
Class 2. For apartment houses and small commercial heating jobs (Capacity 100 to 200
Ib of coal per hour).
Class 3. For general commercial heating and small high pressure steam plants (Capacity
200 to 300 Ib of coal per Hour)".
Class 4. For large commercial and high pressure steam plants (Capacity over 300 Ib of
coal per hour).
4 • What main parts are found in an underfeed residential stoker?
A hopper is supplied to hold coal which is fed by a screw >or plunger into a retort provided
with air openings called tuyeres. A Uower supplies air under pressure for combustion, and
a gear case provides for changes in coal feeding rates.
5 • What is a dead-plate?
A dead-plate is a flat surface without air supply openings upon which the fuel rests while
combustion of the fixed carbon is completed. Generally the ash is removed from the
dead-plate. ' v »
6 • What rate of coal burning is usually recommended for small underfeed
stokers?
For continuous operation, 25 Ib per square foot of grate surface is recommended; for
short duration peaks, 30 Ib.
476
CHAPTER 28 — AUTOMATIC FUEL BURNING EQUIPMENT
7 • What methods of oil atomization are used?
1. Throwing the oil from a rotating cup or disc.
2. Forcing the oil under high pressure through a whirl chamber in a nozzle.
3. Propelling the oil with a high velocity jet of air or steam.
4. Forcing an oil and air mixture through a nozzle.
8 • What is the purpose of atomization?
Atomization is used to increase the surface area of the oil in order to facilitate putting it
into a vaporous state so it may burn.
9 • Is the furnace of much importance in oil burning?
In most cases it is very important. It is the function of the oil burner to supply the air
and fuel in correct proportions ; the furnace must provide heated space for proper mixing
and combustion.
10 • Which flame is considered better, the luminous or the non-luminous?
Laboratory tests show that they are equally efficient in the usual installation.
11 • What main precaution is necessary in choosing a boiler for an oil burner?
Since the burner output is usually varied through a wide range under control of the
thermostat, a boiler should be provided with enough indirect heating surface to absorb
the heat as it is released. The combustion space must be large enough, and have correct
proportions for mixing fuel and air at high temperatures. If oil is used inefficiently
high heating costs will result.
12 • How should oil burner adjustments be made?
Adjustments should be made by an experienced man who uses a gas analysis apparatus
to determine the CO-i content.
13 • What CO2 content should be attained in oil burning?
Ten per cent COz is considered good practice, for it indicates the supplying of 50 per cent
excess air.
14 • What maximum heat release is considered good practice in oil burning?
"A heat release of 38,000 Btu per cubic foot per hour is considered to be the maximum for
average large installations. This figure has been greatly exceeded in some cases, ^ The
design of the combustion chamber, as to impingement of flame and as to proper mixing
at high temperatures, has much to do with the attainable heat release.
15 • Name five types of gas-fired space heaters.
a. Parlor furnaces or circulators.
b. Radiant heaters.
c. Gas-fired steam or hot water radiators.
d. Warm air radiators.
e. Garage heaters.
16 • How are gas heating units rated?
Gas-fired units are rated on the basis of output in Btu per hour.
17 • What safety consideration is noted in establishing the ratings of gas-fired,
units?
The rating is limited by the amount of gas that can be burned without the liberation of
harmful amounts of carbon monoxide,
477
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
18 • What control equipment is essential in the usual oil burner installation?
See Chapter 14. Usually a room thermostat, a limiting device to prevent the pressure or
temperature from exceeding a desirable limit, a shut-off device to guard against failure
of flame ignition, and in steam or hot water boilers a low water protective device.
19 • In the construction of gas-fired garage space heaters, what special pre-
caution must be taken?
A safety screen must be placed over each opening into the combustion chamber to pre-
vent explosions of any possible gasoline vapors.
20 • List some factors which might account for possible economies of stoker
firing over hand firing.
a. The regular feed of coal instead of the intermittent feed.
&. The use of cheaper sizes and grades of fuel.
c. The absence of door openings for firing purposes, which avoids the admission of cold
excess air.
d. The avoidance of overheating because the stoker responds quickly to automatic
equipment controlled by the heat demand.
478
Chapter 29
FUEL UTILIZATION
Heat Loss, Calorific Values, Heating Efficiencies, Non-Heating
Periods, Heat Capacity oj Buildings, Miscellaneous Factors, Degree-
Day Method, Rough Approximations, Relative Heating Costs
TO predict the amount of fuel likely to be consumed in heating a
building during a normal heating season, it is necessary to know the
total heat requirements of the building and the utilization factor of the
fuel. The accuracy of the estimate will depend on the ability to select
these values and on the care taken in making allowances for other variable
factors.
Fuel requirements1 are given by the following general equation :
H X (* - fa) X N m
(t - /0) X C X E v '
where
F = quantity of fuel required for a heating season.
N = number of hours of heating season.
t — inside temperature, degrees Fahrenheit.
^ = average outside temperature, degrees Fahrenheit,
*o = outside design temperature, degrees Fahrenheit.
H — calculated heat loss of building based on outside temperature of £Q, Btu per hour.
C = calorific value of one unit of fuel, the unit being the same as that on which F
is based.
E — efficiency of utilization of fuel, per cent.
HEAT LOSS
The hourly heat loss (H) is equal to the sum of the transmission losses
(fit) and the infiltration losses (Hi) of the rooms or spaces to be heated,
and the total equivalent heating surface required is equal to sq ft.
In estimating the fuel consumption of a building of more than one room
divided by walls or partitions, it is not correct to use the calculated heat
loss of the building without making the proper allowance for the fact that
the heating load at any time does not involve the sum of the infiltration
losses of all of the heated spaces of the building but only part of the
infiltration losses. This is explained in Chapter 6.
It is sufficiently accurate in most cases to consider only half of ^the total
infiltration losses of a building having interior walls and partitions, and
the value of H in Equation 1 would, under these conditions, be equal to
^or further information on this subject see Estimating Fuel Consumption, by Paul D. Close, (Heating
Piping o.nd Air Conditioning, May, 1931).
479
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Ht + -7T1 . If a building has no interior walls or partitions, whatever air
2>
enters through the cracks on the windward side must leave through the
cracks on the leeward side, and only half of the total crack should be used
in computing the infiltration for each side and end of the building. Under
these conditions it is sufficiently accurate to use the total calculated heat
loss (IT) for the building. If the average wind velocity during the heating
season differs from that upon which Hi was derived, the value of H should
be corrected accordingly.
Of course, where the required heating surface is estimated by empirical
or rule-of-thumb methods, refinements in approximating fuel consump-
tion are not warranted, but rule-of-thumb methods often lead to unsatis-
factory results and should be avoided in heating work where more accurate
methods are available. It should be emphasized that the value of H in
Equation 1 is the total heat loss of the building after making the proper
allowance for infiltration.
CALORIFIC VALUES AND HEATING EFFICIENCIES
The calorific values of fuel oils and gas can be ascertained with reason-
able accuracy. The values for various grades of oil are given in Table 3,
Chapter 27. The calorific value of gas can always be obtained from the
local utility company. Values for natural gas are given in Table 4,
Chapter 27; manufactured gas usually has a calorific value of about 535.
Coals have a larger range and may vary for the same type of coal, depend-
ing on its ash content. For general purposes where specific data are
lacking, values can be taken from Table 1, Chapter 27.
To decide on the correct efficiency to use is a more difficult matter, par-
ticularly if the estimate is being made without a full knowledge of the
equipment for burning the fuel and the care the furnace will receive.
Efficiencies usually are given in the catalogs of manufacturers of furnaces
and boilers, but these values are obtained under test conditions and do not
allow for poor attendance, defects in installation, or poor draft. On the
other hand, such efficiencies assume that all the heat radiated from the
outside of the heaters or casings as sensible heat of the flue gases is lost,
whereas, if the heater is installed in the building being heated, a con-
siderable portion of these losses may help to heat the building2; how much
of this it is legitimate to use in increasing the value of E will depend on
whether H included the heat losses in the cellar, and on the construction
of the chimney. Except for an interior chimney, the heat transferred
through the chimney wall to the building will be very small. Chimney
allowances should be greater for lower test efficiencies. Thus an insulated
furnace will give a high efficiency on test but will not heat the cellar. A
modern gas furnace will have a high efficiency with a correspondingly low
flue gas temperature and hence there will be very little heat from the
flue pipe.
For great exactitude the value for E should take care of inefficiency in
the heat distribution in the building because of such losses as excessive
heating of the walls behind the radiators and excessive stratification. It
'Analysis of the Over-All Efficiency of a Residence Heated by Warm Air, by A. P. Kratz and J. F.
Quereau (A.S.H.V.E. TRANSACTIONS, Vol. 35, 1929).
480
CHAPTER 29 — FUEL UTILIZATION
is preferable, however, to include these losses in the value of H, and to
limit E to the fuel burning equipment.
Automatic fuel burning equipment, whether for coal, oil or gas, will tend
to save fuel and will therefore produce a higher efficiency if thermostati-
cally controlled, but on the other hand automatic equipment tends to
make the householder prolong his heating season and maintain a higher
temperature in the house in the early fall and late spring.
NON-HEATING PERIODS
Obviously, the theoretical fuel consumption will be reduced con-
siderably by not operating the heating plant at night. Allowance for
this may be made in either of two ways : (1) by estimating the average
inside temperature t, or (2) by arbitrarily assuming a certain reduction
in the fuel consumption.
The first procedure is, of course, the more accurate. If, for example, the
daytime temperature is to be 70 F, and the temperature from 12 midnight
to 6 a.m. is to be maintained by thermostatic control 'at 50 F, then the
average daily inside temperature t will be ~- or 65 F.
Strictly speaking, this average inside temperature would apply only when
the outside night temperature averages below 50 F, but this -fact usually
is not of sufficient importance to warrant consideration. If the average
outside temperature during the heating season is 30 F, the fuel saving
f-rr\ £> pr
would be approximately 100 X ^ ™ or 12.5 per cent. In this case, the
/U — oU
additional saving in fuel due to the cooling of the air and structural
materials to 50 F would be offset by the heating-up load in the morning.
As to the second procedure, it may be arbitrarily assumed that a
saving in the fuel consumption of from 10 to 30 per cent, depending on
conditions, will result if the heat is shut off after working hours, and the
building is heated to the required temperature during the period of occu-
pancy each day. This, of course, is a general statement and wherever
possible the average temperature should be estimated from the propor-
tionate lengths of the occupancy and non-occupancy periods and the cor-
responding temperatures for these periods. Any deviation from the assumed
inside temperature will result in a variation in the estimated fuel con-
sumption.
HEAT CAPACITY OF BUILDINGS
The heat required to warm the cold building and contents is a factor
to be considered. Under certain conditions, the cooling of the structure
and contents will, to some extent, compensate for the heat required to
rewarm the building. For example, if the building is under thermostatic
control and the day and night temperatures are say 70 F and 50 F,
respectively, there will be a, period during which no heat will be called for
while the building is cooling to 50 F, and the saving resulting therefrom will
correspond to the additional heat required to bring the building and con-
tents back to the daytime temperature. If in estimating the fuel con-
sumption the average daily inside temperature is based on the proper day
and night temperatures and periods, the heat required to warm the
structure may be neglected.
481
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Where irregular conditions are involved it may be desirable to actually
calculate the fuel required to warm the building structure and contents
for the number of times during the heating season the heating plant would
not be in operation and to add this quantity to the fuel required for the
number of hours during which the building is heated. The greater the
heat capacity of the structure the greater will be the relative importance
of this item. For structures of low heat capacity, such as frame buildings,
this factor usually may be neglected.
Example 1 . A small factory building located in Philadelphia is to be heated to 60 F
between the hours of 7 a.m. and 7 p.m., and to 50 F during the remaining hours. The
calculated hourly heat loss, based on a design temperature of — 6 F, is 500,000 Btu. If
coal having a calorific value of 12,500 Btu per pound is fired, and the over-all heating
efficiency is assumed to be 60 per cent, how many tons of coal will be required for a
normal heating season, neglecting other heat sources and any loss of heat through open
windows?
Solution. Since there are no partitions in this building, the entire heat loss is con-
sidered. The average outside temperature during the heating season Za is 41.9 F (see
Table 2, Chapter 7); t = 60 F; N « 5040; H = 500,000; (t - /0) = 66 F; C = 12,500;
E = 0.60. Substituting these values in Equation 1 and dividing by 2000 to change to
tons:
„ 500,000 X 18.1 X 5040 - .
F ~ 66X12,500X0.60X2000 = 46 t0nS °f C°al
Inasmuch as the building will be heated to 50 F at night, the average inside tempera-
ture at the breathing line will be 55 F, and the percentage saving will be QQ _ A-\ Q
= 0.276 or 27.6 per cent. The net fuel consumption will therefore be 46 - 0.276 X 46
or 33.3 tons.
MISCELLANEOUS FACTORS
There are many factors which would be likely to affect the theoretical
fuel requirements of a building, such as the opening of windows, abnormal'
inside temperatures, other heat sources, sun effect, wind, and rain. In
many cases it is difficult to evaluate these factors accurately, particularly
in the case of open windows, and the results are correspondingly less
accurate. The degree of refinement of the calculations should, of course,
be consistent with the conditions involved. If the heat loss from the
boiler and piping does not warm the building or is not included in £T,
the proper allowance should be made. In selecting a boiler, this allowance
is frequently assumed to be 25 per cent of the total heat loss of the build-
ing, but in estimating fuel requirements, the more accurate procedure of
computing the pipe and boiler losses should be used, unless this item is
likely to be outweighed by other less tangible factors.
Where temperature control is installed the fuel consumption can
obviously be predetermined with greater accuracy than where no such
control has been provided. In fact the calculated requirements agree to a
remarkable extent in many cases with the actual fuel consumption. This
has been particularly true of gas-fired installations, with which effective
temperature regulation usually is possible.
OTHER HEAT SOURCES
Where other heat sources are available it is quite often possible to make
accurate allowance for the reduction in the fuel consumption resulting
482
CHAPTER 29 — FUEL UTILIZATION
therefrom. These sources include the heat supplied by persons, lights,
motors and machinery, and should also be ascertained in the case of
theaters, assembly halls and industrial plants. (See Chapter 7.) In many
cases these heat sources should not be allowed to affect the size of the in-
stallation of heating equipment, although they may have a marked effect
upon the fuel consumption. In residences this factor usually may be
neglected.
DEGREE-DAY METHOD
A very useful unit for estimating fuel consumption, particularly for
residences, is the degree-day. (See definition in Chapter 41.) Degree-days
for various cities in the United States and Canada are given in Table 1.
The term degree-day originated in the gas industry and was later stand-
ardized by the American Gas Association*.
The base of 65 F is used for an inside temperature of 70 F. This base
was chosen because it was demonstrated, by means of data collected from
numerous installations, that heat is seldom supplied to a residence when
the outdoor temperature is greater than 65 F. It was also found that
the fuel consumed varied almost directly with the difference between
65 F and the outside temperature.
If the inside temperature were maintained at 70 F throughout the 24
hours of the day, then the base of 65 F would probably be in error. It
must be borne in mind, however, that although the temperature head is
the difference between the inside temperature of say 70 F, and the outside
temperature, a lower temperature than 70 F will usually be maintained at
night and the base of 65 F will therefore allow for this condition. As
already indicated, a temperature of 50 F from midnight to 6 a.m. will
reduce the 24-hour average from 70 to 65 F. It is important to note that
the degree-day applies specifically to an inside temperature of 70 F,
which is the usual temperature for residences, and it should also be noted
that allowance is automatically made for the lower nighttime tempera-
ture, although this allowance is constant for any given locality.
In Equation 1, the quantity (t — 4) X ^V is equivalent to the number
of degree-days D in a heating season multiplied by 24, when the average
daily value of t is 65 F. Therefore,
(t - /a) X N - 24 D (2)
Substituting the value of (t — 4) X N from Equation 2 in Equation 1,
the following general formula for an average daily inside temperature of
65 F, which is approximately equivalent to an inside daytime temperature
of 70 F for residences, is obtained:
Fd " '(t - fc) X C X E (3)
Example 2. The calculated hourly heat loss of a residence located in Chicago is
127,000 Btu, which includes 28,000 Btu for infiltration. The design temperatures are
— 8 If and 70 F. The normal heating season is assumed to be 210 days (5,040 hours) and
the average temperature during this period is 36.4 F (see Table 2, Chapter 7). The
*See Industrial Gas Series, House Heating (third edition) published by the American Gas Association,
483
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 1. DEGREE-DAYS FOR CITIES IN THE UNITED STATES AND CANADAa
Col. A
ColB
ColC
Col A
ColB
Col. C
State
City
Degree-Days
State
City
Degree-Days
Ala.
Birmingham
2,408
Nev. .
Reno
5,891
Mobile
1 471
N H
Concord
6,852
Ariz
Flagstaff
7,145
N. T
Atlantic City
5,175
Tucson
1 845
Trenton
4,934
Ark
Hot Springs
2,665
N M.
Santa Fe
6,063
Little Rock
2811
N Y
Albany
6,889
Calif.
Los Angeles
1,504
Buffalo
6,821
San Francisco
3264
New York ...
5,348
Colo
Colorado Springs
6553
N. C.
Raleigh
3,234
Denver
5 873
Wilmington
2,302
Conn
New Haven
5 895
N Dak
Bismarck
8,498 '
D C
Washington
4626
Ohio
Cincinnati
4,702
Fla
Jacksonville
890
Cleveland
6,154
Ga
Atlanta ....
2,891
Columbus
5,323
Savannah
1,490
Okla.
Oklahoma City
3,613
Idaho
Boise
4,558
Ore
Portland
4,468 '
Lewiston
4924
Salem
4,629
111.
Chicago
6,315
Pa
Philadelphia
4,855
Springfield
5,370
Pittsburgh .
5,235
Ind
Evansville
4 164
R I.
Providence
6,014
Indianapolis
5,297
S. C..
Charleston .•.
1,769
Iowa
Des Moines
6,373
Spartanburg.
3,257
Sioux City
7,023
S. Dak.
Sioux Falls
7,683
Kans.
Dodge City
5,034
Tenn
Memphis
2,950
Topeka .
5,301
Nashville
3,578
Kv
Lexington
4616
Texas
Austin
1,578
Louisville
4,180
Dallas
2,455
La
New Orleans
1,023
Houston
1,157
Me.
Eastport
8,531
San Antonio .
1,202
Portland
7,012
Utah
Logan
6,735
Md.
Baltimore
4,333
Salt Lake City
5,553
Mass.
Springfield
6,464
Vt. .
Burlington
7,620
Boston
6,145
Va. ..
Fredericksburg
4,243
Mich
Detroit
6494
Norfolk
3,349
Marquette .
8,692
Richmond
3,725
Minn
Duluth
9,480
Wash
Seattle
4,868
Minneapolis
7,851
Spokane
6,353
Miss
Vicksburg
1,822
W. Va
Morgantown
5,016
Mo. .
Kansas City
5,202
Parkersburg
4,884
St. Louis
4,585
Wis
Fond du Lac
7,612
Mont
Billings.
7,115
Green Bay. . .
7,823
Havre
8,699
La Crosse
6,690
Nebr
Lincoln.
6,231
Milwaukee
7,372
Omaha
6,128
Wyo. . .
Cheyenne
7,462
Province
City
Degree-Days
Province
City
Degree-Days
B. C
Victoria
5,777
Ont.
Toronto
7,732
Vancouver
5,976
Que
Montreal
8,705
Kamloops .
6,724
Quebec
8,628
Alb.
Medicine Hat
8,152
N. B.
Fredericton
9099
Sask.
Ou'AoDelle
11,261
N. S. .
Yarmouth
7,694
Man. .... .
Winnipeg
11,166
P.E.I. ...
Charlottetown
8,485
Ont
Port Arthur
10,803
aFrom Industrial Gas Aeries, House Heating (third edition) published by the American, Gas Association.
These degree-days are based on daily 'mean temperatures. Base, 65 F.
484
CHAPTER 29 — FUEL UTILIZATION
building is to be heated with oil fuel having a calorific value of 141,000 Btu per gallon.
The heating efficiency is assumed to be 70 per cent. Thermostatic control is to be used
and a temperature of 55 F is to be maintained from 11 p.m. to 7 a.m. How many gallons
of oil will 'be required during a normal heating season if the loss of heat through open
windows is neglected?
Solution. The maximum hourly heat loss will be 127,000 - = 113,000 Btu
2t
= H. Substituting the proper values in Equation 1:
113,000 X (70 - 36.4) X 5040
F = 141,000 X 0.70 X [70 - (- 8)1 = 2486 gal °f Olh
T« . . , , .„ ,70 X 16 + 55 X 8 _ «
The average inside temperature will be - ^7 - = 65 F
and the fuel saving due to this fact will be ^ - 5— = 0.149 or 14.9 per cent.
—
Hence, the net fuel consumption will be 2486 — 0.149 X 2486 = 2116 gal. -
The normal number of degree-days for Chicago is 6315. Substituting in Equation 3
and solving by the degree-day method:
_, 113,000 X 6315 X 24 OOOK . , ..
F = 78 X 141,000 X 0.70 = 2225 gal °f Ol1
No allowance need be made for the average temperature of 65 F since this is taken
care of by the selection of a base of 65 F for the degree-day, as already explained. It will
be noted that the two methods check within 5 per cent in this case. If the average daily
inside temperature in the first solution had been 66.4 F instead of 65 F, the two methods
would have checked exactly.
INDUSTRIAL DEGREE-DAY
Since the standard degree-day is intended for an inside temperature of
70 F, it is particularly convenient for solving residence problems. Where
the design temperature differs greatly from 70 F, the standard degree-day
cannot be accurately applied* Consequently, the industrial degree-day4
has been developed and values have been derived for two bases, namely
55 F and 45 F, intended for inside temperatures of 60 F and. 50 F, re-
spectively.
There is a considerable spread, however, among these three bases, and
consequently there would be an appreciable error if the actual basis to be
used in a certain case would be approximately midway between any two
of the three bases for which degree-day values are at present available.
Since the correction cannot be made on a proportionate basis, it would be
more accurate in the majority of cases involving inside temperatures other
than 70 F, 60 F, or 50 F to apply Equation 1.
APPROXIMATING FUEL REQUIREMENTS
It is sometimes desirable to obtain a rough approximation of the annual
fuel consumption. Such approximations may be obtained by using unit
factors based on the fuel requirements per square foot (or per 100 sq ft) of
radiation or per 1000 cu ft of space.
Fig. 1 may be used for rough approximations of coal and oil require-
4See Heating and Ventilating Degree- Day Handbook,
485
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
ments. It should be noted that this figure is given in terms of the fuel
consumption per 1000 degree-days per 100 sq ft of equivalent heating
surface (steam) based on an emission of 240 Btu per square foot. Unless
the radiation is calculated with reasonable accuracy, unit factors will be of
little value even for rough approximations, since it is obvious that such
radiation requirements must bear some relationship to the actual heating
requirements of the building.
Example 3. Estimate the approximate coal consumption for a building located in
New York City in which the calculated heating surface requirements (steam) are
1000 sq ft based on design temperatures of zero and 70 F.
Tons of Coal per 1000 Defr-Days per 100 Sq. Ft of Heating Surface,
240 B. t. u. per sq. ft
D p p p a
5 g S S 8
-
/
s § s g s s
Gals, of Oil per 1000 Deg.-Days per 100 Sq Ft of Heatmg Surface,
240 B. t. u. per sq ft
/
-
/
•
-
/
/
-
y ,
/
-
/
~"
/
/
I
-^
/
-10
0, +10
Outside Design Temp., deg. fahr.
+20
FIG. 1. CURVE FOR OBTAINING ROUGH APPROXIMATION OF ANNUAL FUEL CONSUMPTION
IN TONS OF COAL OR GALLONS OF OIL PER 1000 DEGREE- DAYS PER
100 SQ FT OF EQUIVALENT STEAM HEATING SURFACE**
aThis curve is based on heating efficiencies of 60 and 70 per cent for coal and oil, respectively, a calorific
value of coal of 13,000 Btu per pound, a calorific value of oil of 140,000 Btu per gallon, an inside tempera-
ture of 70 F, and an emission of 240 Btu per equivalent square foot of heating surface (steam), and does not
allow for unusual factors which would affect the fuel consumption, such as open windows, week-end shut-
downs, etc. For hot water, divide the result obtained by means of this chart by 1.6.
Solution, From Fig. 1, the fuel consumption for a design temperature of zero is 0.53
tons per 1000 degree-days per 100 sq ft of heating surface. Since there are 5348 degree-
days in New York City in a normal heating season, the fuel consumption will be approxi-
mately 0.53 X 5.348 X 10 = 28.34 tons.
Fig. 2 is taken from the 3rd edition of Industrial Gas Series on House
Heating, published by the American Gas Association, and indicates the
average gas consumption per degree-day for various heat contents.
While the fuel consumption in individual cases may vary somewhat from
the curve values, these average values are sufficiently accurate for esti-
mating purposes and give very satisfactory results.
The value generally used in the manufactured gas industry for resi-
dences is 0.21 cu ft per degree-day per square foot of equivalent steam
486
CHAPTER 29 — FUEL UTILIZATION
radiation (240 Btu) based on the theoretical requirements. A correction
for warmer climates is necessary and it is customary to gradually increase
the relative fuel consumption below 3,000 degree-days to about 20 per
cent more at 1,000 degree-days.
For hot water or warm air heat the fuel consumption is about 0.19 cu ft
per degree-day per square foot of equivalent steam radiation, that is, per
240 Btu per hour. The actual requirements likewise relatively increase
with hot water or warm air systems as the number of degree-days de-
creases below 3,000. For larger installations, that is, 1,000 sq ft of
D
o:
I
200 300
r-cu-'m OF CAS PER SQ. FT. INSTALLED
OT WATER RADIATION ,
IHOT
2-CU FT. OF GAS PER 5<5>. FT. INSTALLED
i i i STEAM RAD.IATION ,
3 -CU. FT. OF GAS PER 100 CU> FT. BLDC.
| | CONTENTS HOT. AIR. SYSTEM. ,
4-CU.FT. OF GAS PER 1000 B.T.U. HOURLY
LOSS FROM BLDG- HOT AIR SYSTEM
400 500 600 700 800
B.T.U. VALUE OF GAS
900 1000
FIG. 2. CHART GIVING GAS REQUIREMENTS PER DEGREE-DAY FOR VARIOUS CALORIFIC
VALUES OF GAS AND FOR DIFFERENT HEATING SYSTEMS*
aThis chart is based on an inside temperature of 70 F and an outside temperature of zero. If the radia-
tion is installed on the basis of any other temperature difference, multiply the result obtained from this
chart by 70, and divide by the actual temperature difference.
theoretical radiation and above, there is an increase in efficiency, and a
consequent decrease in the fuel consumption per degree-day per square
foot of heating surface.
The approximate quantities of steam required in New York City per
square foot of heating surface for various classes of buildings are given in
Chapter 37.
The preceding discussion on fuel consumption has dealt with the heating
requirements of the building irrespective of any air that may be intro-
duced for ventilation purposes other than the normal infiltration of out-
side air. The heat required for warming air brought into the building for
ventilation may be estimated from data given in Chapters 2 and 22.
487
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
RELATIVE HEATING COSTS
A comparison of the relative cost of heating with different fuels can
be made with even a fair degree of accuracy only when there is a full
knowledge of the equipment which will be used with each fuel, and the
efficiency with which each will be operated. When proposing to sub-
stitute one fuel for another, the yearly cost with the fuel being used can be
obtained. The accuracy of the comparison will depend upon the care
taken in estimating the cost of the new fuel with the equipment which
will be used.
A convenient basis for comparison of various fuels is the cost per
million Btu. The formula used in estimating costs for coal is:
Y - 500XC (4)
* ~ CcXEc W
where
X — cost of heating with coal in dollars per million Btu.
c = cost of coal in dollars per ton.
Cc = calorific value of coal, Btu per pound.
EC = over-all or house efficiency for coal, expressed as a decimal.
Example 4. If coal having a calorific value of 13,000 Btu per pound costs $10.00 per
ton, the cost per million Btu, assuming an efficiency of 60 per cent, will be:
50° X< - n 64
_ _
~ 13,000 X 0.60
The formula used in estimating costs for oil is :
_
C0 X W X £0
where
Y = cost of heating with oil in dollars per million Btu.
p — cost of oil in dollars per gallon.
C0 — calorific value of oil, Btu per pound,
W — weight of oil per gallon, pounds.
Eo - over-all or house efficiency for oil, expressed as a decimal.
Example 5. If oil having a calorific value of 141,000 Btu per gallon (C0 X W)^ costs
10 ji per gallon, the cost per million Btu, assuming an efficiency of 70 per cent, will be:
1,000,000x0.10 ,
y 141,000 X 0.70
The formula used in estimating costs for gas is:
--cr^ »
where
Z = cost of heating with gas in dollars per million Btu.
g = average cost of gas, including demand and commodity charges, dollars per
thousand cubic feet.
Cg = calorific value of gas, Btu per cubic foot.
E% =s over-all or house efficiency for gas, expressed as a decimal.
Example 6, If manufactured gas, having a calorific value of 535 Btu per cubic foot,
costs 60? per thousand cubic feet, the cost per million Btu, assuming an efficiency of
80 per cent, will be:
535 X'0.80
488
CHAPTER 29 — FUEL UTILIZATION
PROBLEMS IN PRACTICE
1 • What two factors are most essential in estimating the fuel consumption for
heating a building in a normal season?
The total heat requirements of the building, and the efficiency of combustion.
2 • What will be the cost per year of heating a building with gas, assuming that
the calculated hourly heat loss is 92,000 Btu based on 0 F, which includes
26,000 Btu for infiltration? The design temperatures are 0 F and 72 F. The
normal heating season is 210 days, and the average outside temperature during
the heating season is 36.4 F. The heating efficiency will be 75 per cent. The
heating plant will be thermostatically controlled, and a temperature of 55 F
will be maintained from 11 p.m. to 7 a.m. Assume that the price of gas is
7 cents per 100,000 Btu of fuel consumption, and disregard the loss of heat
through open windows and doors.
The maximum hourly heat loss will be
92,000 - ~^^ = 79>0QO Btu = H.
2>
_ 79,000 X (72 - 36.4) X 24 X 210
100,000 X 0.75 X (72 - 0)
The average inside temperature will be
(72 X 16) + (55 X 8)
24
The fuel saving will be
100 (72 - 66.3) ,c
oco, „,.,„, , 0,
2624'9 hundred th°USatld Btu'
Per Cent'
72 - 36.4
Hence, the net fuel consumption will be
2624.9 - 0.16 X 2624.9 = 2204.9 hundred thousand Btu.
2204.9 X 0.07 = $154.34 = the cost per year of heating the building.
3 • What factors should be taken into consideration when determining the
efficiency at which a fuel will be burned?
Manufacturers' catalogs usually give equipment efficiencies obtained under test con-
ditions. These values do not allow for poor attendance, defects in installation, or poor
draft. Such efficiencies do not consider heat radiated from the outside of the equipment,
but in many cases this heat is utilized.
4 • If 20 tons of coal having a calorific value of 13,000 Btu per pound are burned
in a warm air furnace and produce 286,000,000 Btu at the bonnet, what is the
efficiency of the furnace?
Number of Btu at bonnet
Number of tons X calorific value X number of Ib in one ton
286,000,000 X 100
efficiency.
20 X 13,000 X 2000
= 55 per cent.
5 • In making degree-day calculations, why is the base of 65 F used for an in-
side temperature of 70 F?
This base was chosen because data collected from numerous installations show that heat
is seldom supplied to a residence when the outdoor temperature is greater than 65 F. It
was also found that the amount of fuel consumed varied in almost direct proportion with
the difference between 65 F and the outside temperature.
489
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
6 • Make a rougli approximation of the amount of coal required to heat a
building located in Cleveland, Ohio, assuming that the calculated heating
surface requirements are 500 sq ft of steam radiation based on design tem-
peratures of 70 F and 0 F.
Using Fig. 1, the fuel consumption for a design temperature of 0 F is found to be 0.53
tons per thousand degree-days per hundred square feet of heating surface. Cleveland
has a heating season equivalent to 6154 degree-days, therefore,
0.53 X 6.154 X 5 = 16.31 tons of coal.
7 • Make a rough approximation of the gas required to heat a building located
in Chicago, 111., assuming that the calculated heating surface requirements
are 1000 sq ft of hot water radiation based on design temperatures of 0 F and
70 F. Chicago has 800-Btu mixed gas, and 6315 degree-days.
Using Fig. 2, the fuel consumption for a design temperature of 0 F with 800:Btu gas is
found to be 0.08 cu ft of gas per degree-day per square foot of hot water radiation.
0.08 X 6315 X 1000 = 505,200 cu ft.
8 • A certain building has a maximum heat loss of 250,000 Btu per hour in — 15 F
weather. How many tons of fuel will be required to maintain a temperature of
70 F during a 260-day heating season in which the average temperature is 39 F?
The heating value of the fuel is 13,200 Btu per pound and the efficiency of com-
bustion is 60 per cent.
250,000 (70 - 39) 260 X 24
(70 + 15) 13,200 X 0.60 X 2000
9 • Which item may be determined more closely, the heating value of a fuel or
the efficiency of its combustion?
The heating values of oil, gas, and solid fuels are closely determinate, whereas the
efficiency of burning depends on the particular equipment chosen and the skill used in
handling it.
10 • In an office building, the thermostats are set to maintain 70 F from 7 a.m.
to 5 p.m. and 50 F during the rest of the time. When the outside temperature
is 30 F, how much saving might be expected because the temperatures are
lowered? Under the above conditions the building becomes 50 F by 11 p.m. and
warms up to 70 F by 8 a.m.
A temperature of 70 F is maintained during 9 hours, and one of 50 F during 8 hours; the
temperature would average about 60 F during the 7 hours required for cooling down and
warming up. The average is 60.4 for the 24 hours. (The average temperature calcu-
lated would have been 58.3 F, had the warming and cooling periods been neglected.)
The saving is jj^r X 100 = - X 100 = 24 per cent.
11 • How does the heat capacity of a structure influence the saving made by
carrying lower temperatures during the night?
The heat storage capacity of the walls prevents rapid dropping of temperatures at night-
time and delays the warming up process in the morning. In an extreme case, the building
would not reach the lowered temperature by the time the higher temperature is called
for in the morning. But under any conditions, the saving made by lowering the tem-
perature can be correctly estimated by using the average temperature observed over the
24-hour period as a factor, as in Question 10.
12 • What are some of the miscellaneous factors that may cause actual fuel
consumption to vary from the theoretical fuel requirements as calculated by
the use of heat losses, temperature difference, and fuel burning efficiency?
The opening of windows; abnormally high or low inside temperatures; other sources of
heat, such as machinery or lights; sun effect; and unusual winds.
490
Chapter 30
RADIATORS AND GRAVITY
CONVECTORS
Heat Emission of Radiators and Convectors, Types of Radiators,
Output of Radiators, Heating Effect, Heating Up the Radiator,
Enclosed Radiators, Convectorsy Code Tests, Gravity -Indirect
Heating Systems
THE general terms for heating units are: (1) radiators, for direct sur-
faces, either exposed, enclosed, or shielded; and (2) connectors, or
concealed heaters, for extended surfaces that are built in as part of an
enclosure or cabinet. Some heating units are also available that are a
combination of radiators and convectors.
HEAT EMISSION OF RADIATORS AND CONVECTORS
All heating units emit heat by radiation and conduction. The resultant
heat from these processes depends upon whether or not the heating unit is
exposed or enclosed and upon the contour and surface characteristics of
the material in the units.
An exposed radiator emits less than half of its heat by radiation, the
amount depending upon the size and number of sections. When the
radiator is enclosed or shielded, radiation is further reduced. The balance
of the emission is by conduction to the air in contact with the heating
surface* and the resulting circulation of the air warms by convection,
A built-in heating unit in a con vector emits practically all of its heat by
conduction to the air surrounding it and this heated air is in turn trans-
mitted by convection to the rooms or spaces to be warmed, the heat
emitted by radiation being negligible. The small amount of heat trans-
mitted by radiation to the inside surface of the enclosure diminishes as the
surface temperature of the enclosure approaches the surface temperature
of the heating unit.
TYPES OF RADIATORS
Present day radiators may be classified as tubular, wall, or window
types, and are generally made of cast iron. Catalogs showing the many
designs and patterns available now include a junior size which is more
compact than the standard unit.
Pipe Coil Radiators
Pipe coils are assemblies of standard pipe or tubing (1 in. to 2 in.) which
are used as radiators. In older practice these coils were commonly used
in factory buildings, but now wall type radiators are most frequently used
491
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
for this service. When coils are used, the miter type assembly is to be
preferred as it best cares for expansion in the pipe. Cast manifolds or
headers, known as branch tee-s, are available for this construction.
OUTPUT OF RADIATORS
The output of a radiator can be measured only by the heat it emits.
The old standard of comparison used to be square feet of actual surface,
but since the advance in radiator design and proportions, the surface
area alone is not a true index of output. (The engineering unit of output
is now the Mb or 1000 Btu.) However, during the period of transition
from the old to the new, radiators may be referred to in terms of equivalent
square feet. For steam service this is based on an emission of 240 Btu
per hour per square foot.
TABLE 1. VARIATION IN DIMENSIONS AND CATALOG RATINGS OF
10-SECTiON TUBULAR RADIATORS
No of Tubes
3
4
5
6
7
Width of Radiator., Inches
4.6-5.1
6.0-7.0
8.0-8.9
9.1-10.4
11.4-12.8
Length per Section Inches
2.5
2.5
2.5
2.5
2.5-3.0
HEIGHT WITH LEGS — INCHES
HEAT EMISSION— EQUIVALENT SQUARE FEET
13-14
16-18
20-21
22-23
25-26
30-32
36-38
20
25.0-32.5
30.0-38.3
36.7-45.0
40.0-45.2
50.0-53.5
63.3-62.5
70.0-75.4
28.5
15.0-17.5
20.0-21.3
20.0-26.7
25.0-30.9
30.0-36.7
20.0-22.5
25
25.0-27.5
33.3-35.0
40.0-4:2.5
25.0-31.2
30.0-33.9
32.5-39.8
40.0-48.6
50.0-56.5
30
35
37.5-40.0
50
60
Output of Tubular Radiators
Table 1 illustrates the difficulty in tabulating tubular radiator outputs
since there is so much variation between the products of the different
manufacturers. Only on the four-tube and six-tube sizes is there any
practical agreement in output value. The heat emission values appear as
square feet but are entirely empirical, being based on the heat emission of
the radiator and not on the measured surface.
Output of Wall Radiators
An average value of 300 Btu per actual square foot of surface area per
hour has been found for wall radiators one section high placed with their
bars vertical. Several recent tests1 show that this value will be reduced
from 5 to 10 per cent if the radiator is placed near the ceiling with the bars
horizontal and in an air temperature exceeding 70 F. When radiators
are placed near the ceiling, there is usually so noticeable a difference in
temperature between the floor level and the ceiling that it becomes dif-
ficult to heat the living zone of a room satisfactorily.
University of Illinois, Engineering Experiment Station Bulletin No. 223, p. 30.
492
CHAPTER 30 — RADIATORS AND GRAVITY CONVECTORS
Output of Pipe Coils
The heat emission of pipe coils placed vertically on a wall with the
pipes horizontal is given in Table 2. This has been developed from avail-
able data and does not represent definite results of tests. For such coils
the heat emission varies as the height of the coil. It is customary to use
an average emission of 100 Btu per linear foot of IJ^-in. pipe, 10 ft high.
The heat emission of each pipe of ceiling coils, placed horizontally, is about
126 Btu, 156 Btu, and 175 Btu per linear foot of pipe, respectively, for
1-in., lj^-in., and IJ^-in. coils.
TABLE 2. HEAT EMISSION OF PIPE COILS PLACED VERTICALLY ON A WALL (PIPES
HORIZONTAL) CONTAINING STEAM AT 215 F AND SURROUNDED WITH AIR AT 70 F
Btu per linear foot of coil per hour (not linear feet of pipe)
SIZE OF PIPE
1 IN.
IK IN.
IJilN
Single row
132
162
185
Two .—
252
312
348
Four
440
545
616
Six.
567
702
793
Eight
651
796
907
Ten
732-
907
1020
Twelve
812
1005
1135
Effect of Paint
The prime coat of paint on a radiator has little effect on the heat output,
but the finishing coat of paint does influence the radiation emission. Since
this is a surface effect, there is no noticeable change in the convection loss.
Thus, the larger the proportion of direct radiating surface, the greater
will be the effect of painting on the radiation. Available tests are on old-
style column type radiators which gave results shown in Table 3.
TABLE 3. EFFECT OF PAINTING 32-iN. THREE COLUMN, SIX-SECTION
CAST-IRON RADIATOR*
RADIATOR
FINISH
AREA
QA TTrn
COEFFICIENT
OF HEAT TRANS.
RELATIVE
HEATING VALUE
BTU
PER CENT
1
Bare iron, foundry finish
27
1.77
100.5
2
One coat of aluminum bronze
27
1.60
90.8
3
Gray paint dipped...-
27
1.78
101.1
4
One coat dull black Pecora paint.—
27
1.76
100.0
aComparative Tests of Radiator Finishes, by W. H. Severns (A.S.H.V.E. TRANSACTIONS, Vol. 33, 1927).
HEATING EFFECT
For several years the heating effect of radiators has been considered by
engineers in order to use it for the rating of radiators and in the design of
heating systems. Heating effect is the useful output of a radiator, in the
comfort zone of a room, as related to the total input of the radiator2.
*The' Seating Effect of Radiators, by Dr. Charles Brabble (A.S.H.V.E, TRANSACTIONS, Vol. 33, 1927.
p. 33).
493
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
The results of tests conducted at the University of Illinois are shown in
Figs. 1 and 2s. For the four types of radiators shown, the following con-
clusions are given:
-22
-22
-2.7
-2?
"<?/£/ f?oom
ss J4ZJ&. Test- f?--£:/Q /-Tv&e-F&ne/ F&J.
•• 55O ib.jTe^f ff-Zc, (&csf 223) Wa/J ffbcf.
fiejgh? Abo*? rtoor /n
FIG. 1. ROOM TEMPERATURE GRADIENTS AND STEAM CONDENSING RATES FOR FOUR
TYPES OF CAST-IRON RADIATORS WITH A COMMON TEMPERATURE AT THE 60-lN. LEVEL
Note that the steam condensations are practically the same for all four radiators when the same air
temperature of 69 F i? maintained at the 60-in. level.
6-48 /ty. 7&sf f?-£20t 3 -Tube ftae/-
Test- /?-£-S^-f- T
-tQ/2,343t7fflJO
FIG. 2. ROOM TEMPERATURE GRADIENTS AND STEAM CONDENSING RATES FOR FOUR
TYPES OF CAST-IRON RADIATORS WITH A COMMON TEMPERATURE AT THE 30-lN. LEVEL
Note that the steam condensations are different for all four radiators when the same air temperature of
88 F is maintained at the SO-in. level.
1. The heating effect of a radiator cannot be judged solely by the amount of steam
condensed within the radiator.
2. Smaller fioor-to-ceiling temperature differentials can be maintained with long, low,
thin, direct radiators, than is possible with high, direct radiators.
'Steam Condensation an Inverse Index of Heating Effect, by A. P. Kratz and M. K. Fahneatock
(A.S.H.V.E. TRANSACTIONS, Vol. 37, 1931).
494
CHAPTER 30 — RADIATORS AND GRAVITY CONVECTORS
3. The larger portion of the floor-to-ceiling temperature differential in a room of
average ceiling height heated with direct radiators occurs between the floor and the
breathing level.
4. The comfort level (approximately 2 ft-6 in. above floor) is below the breathing line
level (approximately 5 ft-0 in. above floor), and temperatures taken at the breathing
line may not be indicative of the actual heating effect of a radiator in the room. The
comfort-indicating temperature should be taken below the breathing line level.
5. High column radiators placed at the sides of window openings do not produce as
comfortable heating effects as long, low, direct radiators placed beneath window
openings4.
HEATING UP THE RADIATOR
The maximum condensation occurs in a heating unit when the steam
is first turned on. Fig. 3 shows a typical curve for the condensation rate
in pounds per hour for the time elapsing after steam is turned into a cast-
iron radiator. The data are from tests on old style column type radiators.
fate of Condensation per5q.FtperHr.(inlbJ
o 'o 8 8 fe § § ~g fe 5§ |
/
\
/
\
/
\
/
^
\
/
\
/
\
/
\
\
, >
/
.^
/
I/
**• "0 10 20 30 40
Time elapsing after Siecim is turned in+o Radiortor (m Minutes!
FIG. 3. CHART SHOWING THE STEAM DEMAND RATE FOR HEATING UP A CAST-IRON
RADIATOR WITH FREE AIR VENTING AND AMPLE STEAM SUPPLY
In practice the rate of steam supply to the heating unit while heating up
is frequently retarded by controlled elimination of air through air valves
or traps. Automatic control valves may also retard the supply of steam.
ENCLOSED RADIATORS
The general effect of an enclosure placed about a direct radiator is to
restrict the air flow, diminish the radiation and, when properly designed,
improve the heating effect. Recent investigations5 indicate that in the
design of the enclosure three things should be considered :
1. There should- be better distribution of the heat below the breathing line level to
produce greater heating comfort and lowered ceiling temperatures.
*Effect of Two Types of Cast Iron Steam Radiators in Room Heating, by A. C. Willard and M. K.
Fahnestock (Heating, Piping, and Air Conditioning, March, 1930).
•University of Illinois Engineering Experiment Station Bulletins No. 192 and 223, and Investigation of
Heating Rooms with Direct Steam Radiators Equipped with Enclosures and Shields, by A. C. Willard,
A. P. Kratz, M. K. Fahnestock and S. Konzo (A.S.H.V.E. TRANSACTIONS, Vol. 35, 1929),
495
AMERICAN SOCIETY of HEATING 4nd VENTILATING ENGINEERS GUIDE, 1935
2. The lessened steam consumption may not materially change the radiator heating
performance.
3. The enclosed radiator may inadequately heat the space.
A comparison between a bare or exposed radiator (A) and the same
radiator with a well-designed enclosure (j5)r with a poorly-designed
enclosure (C), and with a cloth cover (D) will illustrate the relative
heating effects. In Fig. 4 the curve (B) reveals that the enclosed radiator
used less steam than the exposed radiator, but gave a satisfactory heating
performance. A well-designed shield placed over a radiator gives about
the same heating effect. Curve (C) shows the unsatisfactory effects
produced by improperly designed enclosures. Curve (D) shows that the
effect of a cloth cover extending downward 6 in. from the top of the
radiator was to make the performance unsatisfactory and inadequate.
TEMPERATURE IN DEG FAHR
8 8 3 8
A-
0<
^
,
^— •*
-^*
^w-+
B
IS
v<
&*A
fc^-
^-"*
^
£
if
X
f^
c
<&
'/&
' *S
?X
.x"
Radiator
Steam consumption
Lb per hr
Per cent
* ,
/
/
A
B
C
D
5.44
4.71
4.50
4.59
100
86.6
82.7
84.4
—
) 2 4 6 8 1
HEIGHT ABOVE FLOOR IN FEET
FIG. 4. STEAM CONSUMPTION OF EXPOSED AND CONCEALED RADIATORS
Practically all commercial enclosures and shields for use on direct
radiators are equipped with water pans for the purpose of adding moisture
to the air in the room. Tests6 show that an average evaporative rate of
about 0.235 Ib per square foot of water surface per hour may be obtained
from such pans, when the radiator is steam hot and the relative humidity
in the room is between 25 and 40 per cent. This source of supply of
moisture alone is not adequate to maintain a relative humidity above
25 per cent on a zero day.
CONVECTORS OR CONCEALED HEATERS
Although any standard heating unit (i.e., radiator) may be concealed
in a cabinet or other enclosure so that the greatest percentage of heat is
"University of Illinois Engineering Experiment Station Bulletin No. 230, p, 20.
496
CHAPTER 30 — RADIATORS AND GRAVITY CONVECTORS
conveyed to the room by convection, the best results are usually
obtained where units of special design are used. Commercially, these
specially designed units are built in as part of the enclosing cabinets which
are necessary for the proper functioning of these heaters. As distin-
guished from radiators, these gravity con vectors have come to be known as
concealed heaters. Fig. 5 shows a typical built-in cabinet convector.
SECTION
FIG. 5. TYPICAL CONCEALED CONVECTOR USING SPECIALLY DESIGNED HEATING UNIT
' The elements or heating units usually consist of a relatively large amount
of extended surface which may be integral with the core or assembled over
it, making thermal contact by pressure, through solder, or by both pres-
sure and metallic contact. Heating elements may be of cast-iron, cast
aluminum, sheet steel, copper, or commercial alloys.
Concealed heaters or convectors maintain room temperatures with low
steam consumption due, probably, to their performance characteristics
which give reduced air temperatures in the upper level of a room with a
directed flow of warm air into the living zone and but little radiant heat to
exposed surfaces. The Concealed Heater Manufacturers Association has
decided to use the A.S.H.V.E. Standard7 in the formulation of its ratings,
but has made a provision that heating effect be included in the ratings in
accordance with the following rules:
" 'A.S.H.V.E. Standard Code for Testing and Rating Concealed Gravity Type , Radiation (A.S.H.V.E.
TRANSACTIONS, Vol. 37, 1931).
497
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Con vectors 20 in. or lower may have a heating effect of 15 per cent included in their
rating; for higher convectors, 1 per cent shall be deducted for each 1 in. increase in
height above 20 in. No heating effect shall be included in the ratings for convectors
with a cabinet 35 in. from the floor to the top, or higher. All ratings published will show
definitely that this heating effect factor is included in the catalog ratings.
Concealed heaters or convectors are generally sold as completely
built-in units. The enclosing cabinet should be designed with suitable
air inlet and outlet grilles to give the heating element its best performance.
Tables of capacities are catalogued for various lengths, depths and heights,
and combinations are available in several styles for installations, such as
the wall hanging type, free-standing floor type, recess type set flush
with wall or offset, and the completely concealed type. Most of these
types may be arranged with a top outlet grille, although the front outlet
is practically standard. In cases where enclosures are to be used but are
not furnished by the heater manufacturer, it is important that the pro-
portions of the cabinet and the grilles be so designed that they will not
impair the performance of the assembled convector.
The output of a concealed heater, for any given length and depth, is a
variable of the height. Published ratings are generally given in terms of
equivalent square feet, corrected for heating effect. However, an extended
surface heating unit is entirely different structurally and physically from
a direct radiator and, since it has no area measurement corresponding to
the heating surface of a radiator, many engineers believe that the per-
formance of convectors should be stated in Btu's. For steam convectors,
as for radiators, 240 Btu per hour may be taken as an equivalent square
foot of radiation.
CODE TESTS FOR RADIATORS AND CONVECTORS
As previously indicated, the output of radiators and convectors is still
designated by the terms of older practice, but this is gradually giving place
to an engineering method of designating heat emission. The A.S.H.V.E.
has adopted the following standards : Code for Testing Radiators (1927) ;
Codes for Testing and Rating Concealed Gravity Type Radiation (Steam,
1932, and Hot Water, 1933).
For steam services the actual condensation weight is taken without any
allowance for heating effect; for hot water services the weight of circulated
water is used without allowance for heating effect. In all cases the total
heat transmission varies as the 1.3 power of the temperature difference
between that inside the radiator and the air in the room, and is expressed
in Btu or Mb per hour.
Standard test conditions specify either a steam pressure of 1 Ib gage
(215 F), or hot water at 170 F and a room temperature of 70 F for radi-
ators, or an inlet air temperature of 65 F for convectors. The heating
capacity of a steam radiator or steam convector is determined as follows:
Ht - Wshfg (1)
where
Ht = Btu per hour under test conditions.
W$ =s condensation in Ib per hour.
hfg — latent heat in Btu per Ib.
498
CHAPTER 30 — RADIATORS AND GRAVITY GONVECTORS
Ht may be converted to standard conditions of code ratings by using
the proper correction factor from the following formulae :
For radiators :
c = P15 - 7oy-3 = / 145 y-8
For con vectors:
r _ /215-65\1.3 _ / 150 \1.3
t-s — I ~~m ^r~ } — I ~^ ^r~ I (*>)
\ TS - TI ) \ rs - TI )
The output under standard conditions will be :
Hs — Cs Ht ^4}
"where
Cs = correction factor.
Ts = steam temperature during test, degrees Fahrenheit.
IV = room temperature during test, degrees Fahrenheit.
T{ = inlet air temperature during test, degrees Fahrenheit.
H3 — heat emission rating under standard conditions, Btu per hour.
Similarly, for hot water convenors, the output under test conditions may
be determined as follows:
H=W (6! - 02) ^~ (5)
where
H = Btu per hour under test conditions.
W — pounds of water handled during test.
6j — average temperature of inlet water, degrees Fahrenheit.
62 ss average temperature of outlet water, degrees Fahrenheit.
/ = duration of test, seconds.
To convert test results to standard conditions, the following correction
factor is used:
170-65 \i-3 / 105
6! - 6, } (6)
—
It has been shown that when the exponent 1.3 is used the range of error
Is less than 5 per cent8.
GRAVITY-INDIRECT HEATING SYSTEMS9
The heating units for this system are usually of the extended surface
type for steam or hot water, and are installed about as shown in Fig. 6.
treats of Convectors in a Warm Wall Testing Booth, by A. P. Kratz, M. K. Fahnestock, and E. L.
Broderick (Heating* Piping and Air Conditioning, August, 1933) .
>For further information on this subject see A.S.H.V.E. Code of Minimum Requirements for the Heating
and Ventilation of Buildings (edition of 1929) and Mechanical Equipment of Buildings* by Harding and
Wfflard, Vol. I, second edition, 1929.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Supports hung from joist o'r floor above
FIG. 6. GRAVITY-INDIRECT HEATING SYSTEM*
aSee Mechanical Equipment of Buildings, by Harding and Willard, Vol. I, second edition, 1929.
The temperature and volume of the air leaving the register must be great
enough so that in cooling to room temperature the heat available will just
equal the heat loss during the same time. In cases where ventilation is a
requirement, the air volume needed may become so large that the entering
air temperature will be but slightly above the room temperature. To
establish and maintain a constant heat flow, provision must be made for
removing the air in the room, after it has cooled to the desired room tem-
perature, by a system of vent flues or ducts. As the air flow is maintained
by natural draft and this gravity head is very slight, it is necessary to
make all ducts as short as possible, especially the runs from the heating
units to the base of the vertical warm air flues. Gravity-indirect arrange-
ments, such as illustrated in Fig. 6, are not to be generally recommended
for hot water systems unless the water temperature can be maintained at
a reasonably high temperature and rapid circulation of the water can be
had.
PROBLEMS IN PRACTICE
1 • What are the principal differences between a radiator and a convector?
A radiator Is commonly thought of as a commercial heating unit having a maximum
amount of direct heating" surface, whereas a convector is a heating device in which the
extended or secondary surface may be several times that of the prime surface. The
radiator ordinarily has vertical tubular chambers for the heating medium but most
convectors have horizontal tubular chambers to which fins are attached so as to form
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CHAPTER 30 — RADIATORS AND GRAVITY CONVECTORS
vertical flues for the passage of air. While radiators are either exposed, enclosed, or
shielded, convectors are concealed by means of a tight-fitting enclosure. Radiators are
commonly made of cast-iron but convectors may be made of a combination of metals,
such as copper and brass, or copper and aluminum.
2 • How did the term heating effect come into use?
It has been found that a room requiring a radiator of a certain determined capacity
could under certain conditions be properly heated, with less temperature gradient be-
tween floor and ceiling and with less steam condensation, by the same radiator or by one
of a different design having the same commercially rated capacity. This resulted in the
use of the term heating effect to apply to the useful heat output of a radiator, in the com-
fort zone of a room, as related to the total input to the radiator.
3 • What is the effect of enclosing a direct radiator?
This will depend almost entirely on the design of the enclosure. If properly enclosed, a
radiator can be made to give better heat distribution below the breathing line and to
condense less steam than does an unenclosed radiator giving equal comfort.
4 • Does paint on a direct radiator affect its heat output?
Aluminum or gold bronze paint tends to reduce the heat output of a direct radiator
perhaps 10 per cent, but ordinary non-metallic paint will have little effect on the heat
output.
5 • How can the temperature gradient between the floor and the ceiling of a
Toom he maintained?
Long, low, thin, direct radiators will maintain smaller floor to ceiling temperature
differences than high direct radiators. Convectors properly selected and properly
installed will accomplish the same result.
6 • Is the method of enclosing a direct radiator different from that required
for a convector?
Generally, yes. An enclosure for a direct radiator should provide a space of at least
2 in. between the radiator and the front and back inside vertical surfaces of the enclosure
to utilize the radiant heat to best advantage in heating the air stream passing through
the enclosure. The enclosure for a convector should be constructed with as little clearance
as possible between the inside vertical surfaces and the convector so as to confine the
passage of the air stream through the fins of the convector. An all-over face grille, often
used when direct radiators are concealed, should never be used for a convector. The
•essential requirements for a convector enclosure are an air inlet below the convector, a
warm air outlet above it, and sufficient height between the openings to provide a stack
•effect.
7 • Is it necessary to make any allowance for the performance of a convector
hecause it is enclosed?
No. The commercial ratings of convectors have been determined by testing the con-
vectors in proper enclosures with grilles in place just as they should be installed for
ordinary service.
$ • On what hasis are the capacities of convectors published?
Published ratings of convectors are on the basis of equivalent square feet of direct exposed
cast-iron. If any allowance is made for heating effect, the amount of such allowance is
generally stated in the manufacturers' catalogs.
9 • How are fins of convectors attached to the tubes or prime surface?
Tubes or a solid core may be forced through piercings in the fins under pressure, or the
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
tubes may be expanded into the holes through the fins. In addition a metallic bonding
agent is sometimes used to insure permanent contact.
10 • What is the procedure in selecting a convector when the required amount
of radiation is known?
First the limiting factor or factors of the enclosure must be determined so the available
size of the wall recess can be found. Manufacturers' catalogs show capacities of con-
vectors of each standard length and depth with varying enclosure heights. From these
capacity tables, the proper convector of the required capacity can be selected for the
available wall recess. If all three dimensions of the wall recess are insufficient to accom-
modate a convector of the required capacity, the available height and length can be
maintained, but greater depth can be obtained by using a partially recessed enclosure.
11 • Given a room to be heated to 80 F with outside temperature at zero F.
Assume the heat loss under these conditions to be 10,000 Btu per hour. Deter-
mine the size of the steam radiator to be installed.
A square foot of radiation is equivalent to a heat emission of 240 Btu per hour under
standard conditions of steam at one pound gage pressure (215 F) and surrounding air
at 70 F. With surrounding air at 80 F, the heat emission from a radiator will be less.
Under these conditions, the heat emission will not be 240 Btu per square foot of catalog
rating per hour, but 240 Cs.
_ («. - 'i)1'3
~~
- 70) ~ '
and 240 Cs = 240 X 0.912 = 218.5 Btu. Therefore, the size of the radiator to be
selected shall have a catalog rating of 10,000 divided by 218.5 or 45.8 sq ft.
Chapter 31
STEAM HEATING SYSTEMS
Gravity and Mechanical Return, Gravity One-Pipe Air-Vent
System, Gravity Two-Pipe Air 'Vent System, One-Pipe Vapor
System, Two-Pipe Vapor System, Atmospheric System, Vacuum
System, Sub -Atmospheric System, Orifice System, Zone Control,
Condensation Return Pumps, Vacuum Pumps, Traps
THE essential features of the common type of steam heating systems
are described in this chapter. They may be classified according to the
piping arrangement, the accessories used, the method of returning the con-
densate to the boiler, the method of expelling air from the system, or the
type of control employed. Information concerning the design and layout
of steam heating systems will be found in Chapter 32.
GRAVITY AND MECHANICAL RETURN
In gravity systems the condensate is returned to the boiler by gravity
due to the static head of water in the return mains. The elevation of the
boiler water line must consequently be sufficiently below the lowest
heating units and steam main and dry return mains to permit the return
of condensate by gravity. The water line difference1 must be sufficient to
overcome the maximum pressure drop in the system and, when radiator
and drip traps are used as in two-pipe vapor systems, the operating
pressure of the boiler. This applies only to closed circuit systems, where
the condensation is returned to the boiler. If the condensation is wasted,
no water line difference is required.
In mechanical systems the condensate flows to a receiver and is then
forced into the boiler against the boiler pressure. The lowest parts of the
supply side of the system must be kept sufficiently above the water line
of the receiver to insure adequate drainage of water from the system, but
the relative elevation of the boiler water line is unimportant in such cases
except that the head on the pump or trap discharge becomes greater as
the height of the boiler water line above the trap or pump increases.
There are three general types of mechanical returns in common use,
namely, (1) the mechanical return trap, (2) the condensation return
pump, and (3) the vacuum return pump. Further information on pumps
and traps will be presented later in this chapter,
GRAVITY ONE-PIPE AIR-VENT SYSTEM
In the gravity one-pipe air-vent system each radiator has but a single
connection through which steam must enter and condensation must
The water line difference is the distance between the water line of the boiler and the low point of the
water in the dry return main.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
return in the opposite direction. Each radiator has an individual air
valve.
Up- Feed Gravity One- Pipe Air- Vent System
This system is the most common of all methods of steam heating, due
largely to its low cost of installation and its simplicity. As will be seen
from Fig. 1, the steam piping rises to a point as high as possible at the
boiler and pitches downward from this location until the far end of the
main or mains is reached. At the far ends drips are taken off at the low
points of the steam mains, are water-sealed below the boiler water line,
and then brought back to the boiler in a wet return. Single pipe risers
AIR VALVE
HARTFORD
RETURM
COMMECTlQh-
FIG. 1. TYPICAL UP-FEED GRAVITY ONE-PIPE AIR- VENT SYSTEM
are branched off the main or mains to feed the radiators, the steam passing
up the riser and the condensation flowing down it. The steam and con-
densation flow in opposite directions in the riser but after the condensa-
tion enters the steam main it flows in the same direction as the steam and
is disposed of through the drip connection at the end of the main. In
buildings of several stories, it is customary to drip the heel of each riser
separately, whereas in one- or two-story buildings this is not necessary.
Both types of branches and risers are shown in Fig. 1.
Horizontal branches to radiators and risers should be pitched at least
Yz in. in 10 ft downward toward the riser or vertical pipe, and the hori-
zontal branches from the steam main should be graded at least this
amount toward the main, except where the heel of the riser is dripped, in
which case the branch should pitch down toward the riser drip (Figs. 2
and 3). The return line, if wet, may be run without pitch or may be
pitched in either direction, but if it is necessary to carry the return main
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CHAPTER 31 — STEAM HEATING SYSTEMS
overhead for any distance before dropping, the return should slope down-
ward with the flow.
The radiator valves may be of the angle-globe or gate type. They
should not be of the straight-globe type because the damming effect of the
raised valve seat interferes with the flow of condensation through the
valve. Graduated valves cannot be used, as the steam valves on this
system must be fully open or closed to prevent the radiators' filling with
water. Air valves may be manual or automatic, with or without a check
to prevent the re-entrance of expelled air. Usually the automatic type is
installed. The greatest source of difficulty with one-pipe steam systems
is that the heat is all on or all off, with no intermediate position possible.
However, intelligent use of the on-and-off method of manual control
gives reasonably satisfactory results.
It is important that the lowest points of the steam mains and heating
units be kept sufficiently above the water line of the boiler to prevent
FIG. 2. TYPICAL STEAM RUNOUT WHERE FIG. 3. TYPICAL STEAM RUNOUT WHERE
RISERS ARE NOT DRIPPED RISERS ARE DRIPPED
flooding, although proper design will eliminate this danger. Usually 18
in. is sufficient but construction limitations frequently make shorter dis-
tances necessary. The distance may be checked in the following manner :
Referring to Fig. 4 it will be seen that the water in the wet return is really in an in-
verted siphon, or U-shaped container, with the boiler steam pressure on the top of the
water at one end and the steam main pressure on the top of the water at the other end.
The difference between these two pressures is the pressure drop in the system, i.e., the
friction of the steam in passing from the boiler to the far end of the main. The water in
the far end will rise sufficiently to overcome this difference in order to balance the pres-
sures, and it will rise enough farther to produce a flow through the return into the boiler
(usually about 3 in. unless the pipes are small or full of sediment), and it will rise still
farther if a check valve is installed in the return so as to obtain sufficient head to lift the
tongue of the check (usually 4 in. will be necessary).
If a one-pipe steam system is designed, for example, for a total pressure drop of J^ Ib,
and utilizes an Underwriters Loop2 instead of a check valve on the return, the rise in the
water level at the far end of the return due to the difference in steam pressure would be
Y% of 28 in., or 3 M in. Adding 3 in. to this for the flow through the return main and 6 in.
as a factor of safety gives 12 y% in. as the distance the bottom of the lowest part of the
steam main and all heating units must be above the boiler water line. The same system,
however, installed and sized for a total pressure drop of J^ Ib, and with a check in the
return, would require J^ of 28 in., or 14 in., for the difference in steam pressure, 3 in. for
the flow through the return, 4 in. to operate the check, and 6 in. for a factor of safety,
making a total of 27 in. as the required distance. Higher pressure drops would increase
the distance accordingly.
5See discussion of piping details in Chapter 32.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
-Steam main
Boiler steam pressure
t-rot
Steam pressure at
end of main
Return water
FIG. 4. DIFFERENCE IN STEAM PRESSURE
ON WATER IN BOILER AND AT END
OF STEAM MAIN
Steam drop to radiators -
FIG. 6. STEAM RUNOUTS DRIPPING MAIN
Pitch—* _ Runout x
-Steam mam
stearn drop to rad^o
FIG. 7. STEAM RUNOUTS WITH MAIN
DRIPPED AT END ONLY
Down-Feed Gravity One-Pipe Air-Vent System
In the overhead down-feed gravity one-pipe air- vent system there is no
change over the up-feed system in the radiators, the radiator valves, the
air valves, or the radiator runouts as far back as the risers. Beyond this
point there are basic differences'. The steam is taken from the boiler and
carried to the top of the building as near the boiler as possible (Fig. 5).
If the run to the main riser is long, or if the riser extends several stories in
order to reach the top, the bottom of the riser should be dripped into the
wet return. The horizontal main is taken off the top of the riser and
grades down from the riser toward all of the drops, each drop taking its
share of the main condensation (Fig. 6), or all of the drops except the last
may be taken from the top of the main (Fig. 7) , the last drop being from
the bottom and serving as a drain for the entire main. As the overhead
SUPPLY RISEJ^
HARTFORD
RETURN
CONNECTION
FIG. 5. TYPICAL DOWN-FEED GRAVITY' ONE- PIPE AIR- VENT SYSTEM
506
CHAPTER 31 — STEAM HEATING SYSTEMS
main does not carry any condensation from the radiators it is immaterial
which method is used. The air vent shown on the main just before the
last drop (Fig. 5) may be placed at this point or it may be located at the
bottom of the drop under the last radiator connection and sufficiently
above the water line of the boiler to prevent flooding.
GRAVITY TWO-PIPE AIR-VENT SYSTEM
The gravity two-pipe system is now considered obsolete although many
of these systems are still in use in older buildings. Separate supply and
AIR VALVE
HARTFORD
RETURM
COHNECTIi
FIG. 8. TYPICAL UP-FEED GRAVITY TWO-PIPE AIR- VENT SYSTEM
return mains and connections are required for each heating unit; air
valves are installed on the heating units and mains; hand valves are
installed on the returns.
Up-Feed Gravity Two-Pipe System
This system (Fig. 8) has a steam and a return connection to each
radiator. The radiator valves for steam, return, and air are the same as
those described for the gravity one-pipe air-vent system. The steam
main is run and pitched in the same manner as in the one-pipe system,
but the returns from each radiator are connected into a separate return
line system which has its risers carried down and joined to a wet return
line under the boiler water line level. Where the return has to be kept
high to function as a dry return, it is advisable to connect the return
risers to the dry return main through water seals about 36 in. deep, as
shown in Fig. 9, to prevent steam from one riser entering another and
closing the air valves on the nearest radiators.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Down -Feed Gravity Two- Pipe System
The steam main in the down-feed system is carried to the top of the
building, and the piping of the steam side is arranged practically as in the
down-feed one-pipe gravity system. The drips at the bottoms of the
steam drops and the runouts to the radiators are similar to those shown
in Fig. 8 for the up-feed gravity two-pipe system. On the return side of
the system, the piping is arranged in exactly the same manner as the
up-feed gravity two-pipe system.
ONE-PIPE VAPOR SYSTEM
A vapor system is one which operates under pressures at or near
atmospheric and which returns the condensation to the boiler by gravity.
The piping arrangement of a one-pipe vapor system is similar to that of
Return from radiators-*^
-Pitch
Clean out ^J±
FIG. 9. METHOD OF CONNECTING TWO-PIPE GRAVITY RETURNS TO
DRY RETURN MAIN
the gravity one-pipe steam system ; in fact, one-pipe gravity installations
may readily be changed to one-pipe vapor systems by making a few
simple alterations. The steam radiator valve is a plug cock which when
opened gives a free and unobstructed passageway for water. The auto-
matic air valve is of special design to permit the ready release of air from
the radiator and to prevent the return of the air after it is expelled. The
air valves on the main are a quick relief type, and the whole system is
designed to operate on a few ounces of pressure.
TWO-PIPE VAPOR SYSTEM
Two-pipe vapor systems may be classified as (1) closed systems con-
sisting of those which have a device to prevent the return of air after it is
once expelled from the system, and which can operate at sub-atmospheric
pressures for a period of four to eight hours depending upon the tightness
of the system, and (2) open systems consisting of those which have the
return line constantly open to the atmosphere without a check or other
device to prevent the return of air, and which operate at a few ounces
above atmospheric pressure.
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CHAPTER 31 — STEAM HEATING SYSTEMS
Under the first classification the essentials are packless graduated
valves on the radiators, thermostatic return traps on the returns, and
traps on all drips unless they are water sealed. Such a system, illustrated
in Fig. 10, should be equipped with an automatic return trap to prevent
the water from backing out of the boiler. In this up-feed arrangement
the supply piping is carried to a high point directly at the boiler and is
graded down toward the end or ends of the supply main, each supply
main being dripped at the end into the wet return or carried back to a
point near the boiler where it drops down below the boiler water line and
becomes a wet return. From this main, runouts are branched off to feed
risers or radiators above, these being graded back toward the steam main
TRAP
DRIPPED
1^
BOILER VATER LIKE
FIG. 10. TYPICAL UP-FEED VAPOR SYSTEM WITH AUTOMATIC RETURN TRAP*
^Proper piping connections are essential with special appliances for pressure equalizing and air elimination.
if they are not dripped at the bottom of the riser, or toward the riser if
the riser heel is dripped. Both conditions are illustrated in Figs. 2 and 3.
Return risers are connected to each radiator on its return end through
thermostatic traps. Their bottoms are connected to the return main
through runouts which slope toward the main. The return main itself is
sloped back toward the boiler if it is carried overhead; if run wet, the
slope may be neglected. An air vent is installed at the point at which the
return main drops below the water line. In the simplest cases this vent
consists of a %-in. pipe with a check valve opening outward, but in
certain patented systems special forms of vent valves, designed to allow
the air readily to pass out of the system and to prevent its return, are
used. A check valve is inserted in the return main at a point near the
boiler and a vertical pipe is run up into the bottom of the return trap,
which usually is located with the bottom about 18 in. above the boiler
water line. Some traps are constructed to permit the bottom's being
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
From steam main
ir vent and check
=====
Main return
•Automatic return trap
sually 18 in.
Boiler water line
FIG. 11. TYPICAL CONNECTIONS FOR AUTOMATIC RETURN TRAP
placed as close as 8 in. above the boiler water line. On the other side of
this connection a second check valve is installed in the main return just
before it enters the boiler (Fig. 11).
Down-Feed Two-Pipe Vapor System
In the down-feed two-pipe vapor system the steam is carried to the top
of the building, the top of the vertical riser constituting the high point of
the system, and the horizontal supply main is sloped down from this
location to the far ends of each branch. The branches are taken off the
main from the bottom or at a 45-deg angle downward, with the runouts
Bottom of
steam drop
Drip trap
Graduated valve
-Connected to dry return
(where connected to wet
return, drip trap may
be omitted)
FIG. 12. DETAIL OF DRIP CONNECTIONS AT BOTTOM OF DOWN-FEED STEAM DROP
510
CHAPTER 31 — STEAM HEATING SYSTEMS
sloped toward the drops (Fig. 6). Thus each branch from the main forms
a drip and no accumulation of water is carried down any one drop.
Another method of running the steam main, which is not considered as
satisfactory but which is practical, is to take the branches off the top of
the main (Fig. 7) and to drip the end of the main through the last riser, as
illustrated in the down-feed one-pipe system detail shown in Fig. 6. If
this is done, the pipe drop at the end or ends of the mains should be
enlarged one pipe size to provide capacity for this concentration of the
main drip.
The steam drops are carried down through the building with suitable
reductions as the various radiator connections are taken off until the
lowest radiator runout is reached. If the drop is only two or three stories
high, the portion feeding the bottom radiator should be increased one
pipe size to provide for draining the riser, and if the drop is over three
stories high it is well to increase the portion feeding the two lowest radi-
ators one or two pipe sizes, especially if the two lowest radiators are small
and the normal size of drop required is 1 in. or less. The bottom of the
steam drops should terminate with a dirt pocket above which a drip trap
connection is located, as shown in Fig. 12. The returns on a down-feed
vapor system are the same as on an up-feed system except that every
steam drop must have a drip at the bottom connected either into the
return through a trap or into a separate water-sealed drip line below the
boiler water line, as illustrated in Fig. 10, in which case the thermostatic
traps may be omitted. The runouts to the radiators and the radiator
connections of the down-feed system are the same as those of the up-feed
system already described.
ATMOSPHERIC SYSTEM
The distinguishing features of the atmospheric system are gravity
return to the boiler or to waste, graduated or ordinary radiator valves, no
automatic air valves on the radiators , thermostatic traps on the radiator
returns, and the venting of all air from the system by means of pipes open
to the atmosphere. The returns are open to the atmosphere at all times,
usually by extending the return risers to the top of the building where
they are either connected together in groups and carried through the roof
or extended through the roof individually. Atmospheric systems, either
up-feed or down -feed, are often used where the condensation is not
returned to the boiler, as in heating systems supplied by high pressure
steam through pressure-reducing valves at locations far from the boilers.
The returns may be delivered back to the boiler, if desired, by condensa-
tion return pumps which are vented to the atmosphere. The return lines
in such systems are simply gravity waste lines in which the condensation
flows entirely by gravity and is not aided by any pressure difference.
The steam side may be run as that for either up-feed or down-feed
two-pipe vapor systems, as the conditions require, and the radiator con-
nections are the same as for vapor systems in that they have graduated
valves on the radiator supply ends and thermostatic traps on the radiator
return ends. All drips from the supply main and the steam side of the
system must pass through thermostatic drip traps before entering the
return system where only atmospheric pressure exists. Fig. 13 illustrates
a typical scheme of piping used on atmospheric systems.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Trap
Trap.
- 4='~
Supply main,
^Air eliminating and pressure
/Trap
- Give good pitch
Trap.
Dry
returnN
X Riser i /'
equalizing device j ;, . L '
fe* note below* dripped .£
j See note below *
^Boiler water line J
^xWet return ^ ^,'
FIG. 13. TYPICAL ATMOSPHERIC SYSTEM WITH AUTOMATIC RETURN TRAP*
«Proper piping connections are essential with special appliances for pressure equalizing and air elimination
TRAP-
HARTFORD
RETURN
CONNECTlOh;
FIG. 14. TYPICAL UP-FEED VACUUM PUMP SYSTEM
512
CHAPTER 31 — STEAM HEATING SYSTEMS
VACUUM SYSTEM
In the vacuum system, a vacuum is maintained in the return line
practically at all times but no vacuum is carried on the steam side, and the
usual accessories include graduated valves on the radiator supply and
thermostatic traps on the radiator return. The air is expelled from the
system by a vacuum pump and all drips must pass through thermostatic
traps before connecting to the return side of the system.
These systems are often fed from high pressure steam mains through
pressure-reducing valves but they may be fed direct from a low-pressure
steam heating boiler as shown in Fig. 14, in which a typical up-feed
vacuum system is illustrated. The supply main slopes down in the
direction of flow; the runouts pitch down toward the riser if the riser is
dripped (Fig. 3) or up toward the riser if the riser is not dripped (Fig. 2) ;
both conditions are indicated in Fig. 14. The matter of dripping the
risers depends largely on the height of the riser and the judgment of the
designer. Ordinarily risers less than three stories high are not dripped
and those more than four stories high are dripped, but there is no set rule
for this. When risers are dripped the runouts from the steam main may
be taken from the bottom if desired and each runout then serves as a drip
for the main.
The risers are carried up to the highest radiator connection and are
connected to the radiator through runouts sloping back toward the riser.
The radiators usually have graduated valves on the supply end, although
this is not absolutely necessary. Angle-globe valves and gate valves may
be used where graduated manual control is not desirable. The return
valves must be of the thermostatic type which will pass air and water but
which will close against the passage of steam.
The return risers are carried down to the basement and are connected
into a common return line, care being taken that no air pockets exist in
the runouts or in the horizontal return main which slopes downward
toward the vacuum pump to which it is connected. The air and water
are taken by the vacuum pump, which discharges the air from the system
and pumps the water back to the boiler, or other receiver, which may be a
feed-water tank or a hot well. It is essential on these systems that no
connection from the supply side to the return side be made at any point
except through a trap.
While the best practice demands a return flowing to the vacuum pump
in an interrupted downward slope, in some cases limitations make it
necessary to drop the return below the level of the vacuum pump inlet
before the pump can be reached. In such event one of the advantages of
the vacuum system is that the return can be raised by the suction of the
vacuum pump to a considerable height, depending on the amount of
vacuum maintained, by means of a lift fitting inserted in the return.
When the lift is considerable, several lift fittings are used in steps (Fig.
15), more successful operation being obtained by this method than when
the lift is made in one step. If the lift occurs close to the vacuum pump,
a special arrangement is used as shown in Fig. 16.
Down -Feed Vacuum System
The piping arrangement for the down-feed vacuum system is similar
on the supply side to the down -feed vapor system in that it has similar
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
runouts, radiator valves, drips on the bottom of the steam drops, and
enlargement of the drops for the lower radiator connections. The return
side of the system is exactly the same as the up-feed system except that
the steam riser drips at the bottom are connected into the return line
through thermostatic traps. It is preferable to take the runouts for the
risers from the bottom or at a 45-deg angle down from the steam main
(Fig. 6) so that they may serve as steam main drips. When this is done
it is practical to run the steam main level if a runout is located at every
change in pipe size, or if eccentric fittings are used (Fig. 17). A slight
pitch in the steam main, however, should be used when possible. An
overhead vacuum down-feed system is shown diagrammatically in Fig. 18.
CLOSE NIPPLE
VERTICAL LIFT TO
BE ONE SIZE. .•
SMALLEC THAN THE
VACUVM
CUFT FITTING
^WvCUUM 2ETUQN
U-UFT FITTING
VACUUM CETUBN
./LIFT FITTING
FIG. 15. METHOD OF MAKING LIFTS
ON VACUUM SYSTEMS WHEN DISTANCE
is OVER 5 FT
FIG. 16. DETAIL OF MAIN RETURN
LIFT AT VACUUM PUMP
ECCENTRIC QEDUONG
(COUPLING.
FIG. 17. METHOD OF CHANGING SIZE OF STEAM MAIN WHEN RUNOUTS
ARE TAKEN FROM TOP
SUB-ATMOSPHERIC SYSTEMS
The sub-atmospheric systems are similar to the vacuum system except
that a pump capable of operating up to 25 in. of vacuum is used, and a
control is placed on the pump so that the vacuum or absolute pressure
carried in the return can be maintained a certain amount below that
existing in the steam line to cause a constant circulation. The traps are
designed to operate in high vacuum. It is apparent that this system
differs from the ordinary vacuum system by having a vacuum on both
sides of the system, instead of only on the return side, in order to secure
control of the heat emission from the radiators and thus to control the
temperature in the building. The system can be operated in the same
manner as the ordinary vacuum system when desired.
In the vacuum system, steam pressure above that of the atmosphere
exists in the supply mains and radiators practically at all times. In the
sub-atmospheric system, steam pressure exists in the steam main and
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CHAPTER 31 — STEAM HEATING SYSTEMS
radiators only during the most severe weather, while under average
winter temperatures the steam is under a partial vacuum which in mild
weather may reach as high as 25 in. This vacuum is largely self-induced
by the condensation of the steam in the system when an inadequate
supply of steam is being furnished through the control valve which admits
it. In the sub-atmospheric system, a control valve is inserted on the
steam main of an ordinary vacuum system near the boiler, a high-vacuum
pump is substituted for the ordinary type and is supplied with a pressure-
difference control, and traps are placed on the radiators and drips which
will operate satisfactorily at any pressure from 5 Ib gage to 26 in. of
vacuum.
Pitch
Loop / Vacuum pump
-fir
FIG. 18. TYPICAL DOWN-FEED VACUUM SYSTEM
The control valve is a special pressure-reducing valve which may be
controlled manually or thermostatically from points selected in the
building. The vacuum pump regulator is simply a diaphragm so ar-
ranged that, when the vacuum in the return line is insufficient to hold the
desired difference in pressure between the steam and return sides of the
system, the vacuum pump is automatically started and the vacuum
increased to the necessary amount. The actual pressure difference main-
tained between the two sides of the system is only enough to secure
adequate circulation and is often about 2 in. of mercury. This fixed
pressure difference between the supply and return sides of the system
results in practically constant circulation under all pressure conditions.
In order to distribute the steam equally when the system is being
warmed up and also to reduce the amount of steam delivered to the
radiators on mild days, orifice plates are used in the graduated radiator
control valves. The heat emitted from the radiators in mild weather and
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
under conditions of high vacuum is not only reduced in proportion to the
difference in the steam temperature between that for 2 Ib gage and for
25 in. of vacuum but it is reduced still further by a reduction in the amount
of steam which can pass through the orifice when the steam is expanded
due to the vacuum. This renders possible the control of heat emission
from the radiators to a point not indicated entirely by the difference in
steam temperatures.
The high-vacuum pumps on this system are equipped with receivers
having float control so that the pump can be placed on a receiver-return-
pump basis at night if desired so no high vacuum will be carried. One
radical difference between this system and the ordinary vacuum system
is that no lifts can be made in the return line. The returns must grade
downward constantly and uninterruptedly from the radiator return
outlet to the inlet on the high-vacuum pump receiver. No attempt should
be made to heat service water on this system unless the steam line for
water heating is taken off the boiler header back of the heating system
control valve, and then only when 2 Ib or more will be carried on the
boiler at all times.
ORIFICE SYSTEM
Orifice systems of steam heating may have piping arrangements
identical with vacuum systems but some of these systems omit both the
radiator thermostatic traps and the vacuum pump in cases where the
returns are wasted to a sewer or delivered to some type of receiver in
which no back pressure exists. The principle on which they operate is
embodied in the well-known fact that an orifice will deliver varying
velocities when the ratio of the absolute pressures on the two sides of the
orifice exceeds 58 per cent. If the absolute pressure on the outlet side is
less than 58 per cent of the absolute pressure on the inlet side no further
increase in velocity will be obtained.
As a result, if an orifice is so designed in size as to exactly fill a radiator
with steam at 2-lb gage on one side and J^-lb gage on the other, the abso-
lute pressure relation is
14.7 + 0.25 on
r- — 90 per cent
14.7 +
Should the steam pressure be dropped to % Ib gage, the pressure on each
side of the orifice would be balanced and no steam flow would take place.
From this it will be seen that if an orifice of a given diameter will fill a
given radiator with steam when there is a given pressure on the main, it is
simply a question of dropping this main pressure so as to fill any desired
portion of the radiator down to the point where- the main pressure equals
the back pressure in the radiator, at which time no steam will be supplied
at all. If orifices throughout a job are designed on a similar basis, all
radiators will heat proportionately to the steam pressure within the limits
for which the orifices are designed.
Some systems use orifices not only in radiator inlets but also at different
points on the main, thus balancing the system to a greater extent. For
example, the system may be designed for a particularly long run involving
an initial pressure of 3-lb gage on the main and 2 Ib at the end of the main,
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CHAPTER 31 — STEAM HEATING SYSTEMS
but each branch from the main may have an orifice for reducing the
pressure at it to 2 Ib-gage. This is particularly useful for branches near
the boiler where the drop in the main has not yet been produced.
Orifice systems using a vacuum pump operate successfully with the
ordinary low vacuum type of pump producing 8 to 10 in. of vacuum.
They are controlled by various means to regulate the steam pressure.
One method is by a thermostat located on the roof to govern the steam
pressure by a combination of outside and inside temperatures; another,
useful on systems without traps and vacuum pumps, controls the steam
pressure manually from temperature indication stations in the building,
or automatically by a thermostatically-controlled pressure reduction
valve or draft regulator on the boiler ; with oil or gas firing, the on-and-off
control or a boiler pressure control may be used.
ZONE CONTROL
Certain portions of a building may require more heat at times than
others but if the whole building is on one general control, such as would
occur with a single piping system with an on-and-off control or with the
sub-atmospheric or the orifice systems, it would be necessary to supply
sufficient heat to accommodate the coldest portion of the building even
though some sections would be overheated. By zoning, each section of a
building may be controlled separately.
The sides of the building with different exposures should be considered
first, because of the varying effects of the wind and sun. With the pre-
vailing winter winds from the northwest, a simple zoning would place the
north and west sides of the building on one system and the south and east
sides on another. If the building is large enough to justify the expendi-
ture, a better arrangement would be to place all north walls on one zone,
all west walls on a second, all east walls on a third, and all south walls on
a fourth.
In case of high buildings, the lowest 8 or 10 stories may be well protected
from wind by surrounding buildings, the next 10 stories may have
moderate exposure, and above this there may be an unobstructed exposure
to gales. On still days the heat demands vertically will vary little, but on
windy days there will be a marked difference in the heat requirements for
the different horizontal sections. In addition, the chimney effect caused
by the difference in density between the warm air on the inside of a
building and the colder air on the outside will give an air movement which
will require zoning to correct. Where such conditions are encountered,
the building should be divided horizontally as well as vertically. An
arrangement of this character would give 12 zones: namely, north, east,
south, and west lower zones; similar middle zones; and similar top zones.
Each zone should constitute an individual and separate system of piping
with its own supply steam valve (controlled by thermostats in its respec-
tive zone) and with its own return or vacuum pump, if one is used-
Certain interior areas, such as basements, light well walls and other
locations where sun and wind do not affect the conditions, should be
placed in still another zone if the most economical results are to be
secured.
Zoning has advantages even where individual thermostatic radiator
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
control is installed whether this be of pneumatic, electric, or the self-
contained radiator valve type. By operating the different zones to
parallel outside temperature requirements, a large part of the load is
taken off the thermostatic controls ; they make fewer operations and the
radiator follows a more even temperature instead of fluctuating from
extreme hot to extreme cold.
CONDENSATION RETURN PUMPS
Condensation return pumps are generally required when the elevation
of the boiler with respect to the heating units is such that the condensate
will not return by gravity, or when the boiler pressure is greater than that
TPAP-
SUPPLY MAINi
DRY RETURN"
f-AUTOMWTC WTER FEEDER
-AIR VENT.
-AUTOMATIC PUrtP 8c RECEIVER
^eYttVSS TO DRAIN
FIG. 19. TYPICAL INSTALLATION USING CONDENSATION PUMP
supplied the heating units, as in a high-pressure boiler installation sup-
plying steam through a reducing valve to the heating units. The con-
densate is commonly returned by gravity to a receiver, vented to the
atmosphere, from which it flows to the pump.
Condensation return pumps are assembled with tank or receiver and
arranged for either continuous operation or for automatic starting and
stopping by float control. Any style of water pump may be employed for
this service, the power available determining whether the mode of drive
snail be steam or electric. The motor-driven, automatic, centrifugal
pump and receiver has found wide acceptance in practice for low pressure
heating systems.
Fig. 19 shows a typical installation using an automatic condensation
return pump and vented receiver, A float control operates the pump
whenever sufficient water accumulates. Condensation return pumps are
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CHAPTER 31 — STEAM HEATING SYSTEMS
suitable for use on systems in which the returns are under atmospheric
pressure. These include atmospheric systems, orifice systems with open
returns, and certain types of vapor systems which operate within a few
ounces of atmospheric pressure, but ordinarily do not carry any sub-
atmospheric pressure. They may also be used on one-pipe and two-pipe
gravity steam systems with a proper arrangement for venting the receiver.
In discharging to waste there is no object in using a condensation pump
unless the discharge mr.ot be elevated.
VACUUM PUMPS
A vacuum heating pump is employed to create a vacuum on the return
end of a system to remove air and water and to return the condensate to
the boiler or to some other intercepting device that may be employed in
plants having mixed systems of heating and other services. Pumps of
this classification may be driven by steam or electricity; they may be
continuous in operation, or automatic with float or vacuum control in one
or more combinations.
For rating purposes3, vacuum pumps are classified as low vacuum and
high vacuum. Low vacuum pumps are those rated under operation at
5^-in. mercury vacuum, and high vacuum pumps are those rated at
vacuums above 5J^ in.
Return line vacuum pumps are classified in the method of their per-
formance as follows:
a. Those which perform the function of air separation under atmospheric pressure.
b. Those which perform the function of air separation under a partial vacuum.
Pumps coming under the first classification will handle vacuum steam
system condensation coming back by gravity at any temperature up to
205 F without either the sealing or the hurling water flashing into steam.
These pumps, to operate under a combined water level and vacuum con-
trol, must be equipped with a float-control receiver between the vacuum
pump and the system, but where they are intended for continuous opera-
tion, they do not require a receiver. Such pumps employ a single vacuum
producer which removes the condensate and air from the system and
delivers it into a separating chamber under atmospheric pressure from
which the condensate is delivered to the boiler or feed water heater. They
are constructed on one of the following evacuating and discharge principles :
1. Hydraulic vacuum producer with one pump impeller.
2. Hydraulic vacuum producer with two pump impellers.
3. Water displacement vacuum producer with two pump impellers.
4. Piston displacement vacuum producer with one pump piston.
The second classification of pumps will handle vacuum steam system
condensation coming back by gravity at any temperature not exceeding
190 F without the flashing into steam of either the sealing or the hurling
water. In order to operate under a combined water-level and vacuum
control, these pumps must be equipped with a float-control receiver
between the vacuum pump and the system; where intended for con-
tinuous operation they do not require a receiver. Such pumps employ a
vacuum producing impeller which removes air from the receiver or
3See A.S.H.V.E, Standard Code for Testing and Rating return line low vacuum heating pump.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
heating system under a partial vacuum and delivers it through an air
separator against atmospheric pressure. The condensate is removed
from the receiver under a partial vacuum by a separate impeller and is
delivered to the boiler or feed water heater. For evacuating and dis-
charge, a water displacement vacuum producer with two pump impellers
is used.
Receiver Capacities for Vacuum Pumps
Where receivers are used in connection with vacuum pumps there is a
definite relation between the capacity of the receiver and the capacity
of the pump. The receiver should have a capacity of not less than 1J^
times the volumetric quantity of condensation per minute and should not
have such a capacity that the pump will empty the receiver in less than
half a minute. Receivers of larger capacities will result in less frequent
periods of operation.
Piston Displacement Vacuum Pumps
Piston displacement return-line vacuum heating pumps may be either
power or steam driven. They should be provided with mechanical
lubricators and their piston speed in feet per minute should not exceed
20 times the square root of the number of inches in their stroke. While
the volumetric displacement for such pumps was formerly figured at 8 to
10 times the volumetric flow of condensation to be handled, the more
efficient thermostatic traps used today in connection with vacuum
heating systems make it possible to change this proportion so that the
volumetric displacement of these pumps may not be less than 6 times the
volume of condensation.
Vacuum Pump Controls
In the ordinary vacuum system the vacuum pump is controlled by a
vacuum regulator which cuts in when the vacuum drops to the lowest
point desired and which cuts out when the vacuum has been increased to
the highest point. This is done largely to eliminate the constant starting
and stopping of the vacuum pump which would occur if the vacuum were
maintained constant. In addition to this control, a float control is in-
cluded which will automatically start the pump whenever sufficient con-
densation accumulates in the receiver, regardless of the vacuum in the
system. This arrangement makes the vacuum pump primarily a con-
densation pump and secondarily an air pump.
On the sub-atmospheric systems the high vacuum pump is controlled
by a differential regulator which keeps the vacuum in the return line
always a few inches higher than that in the steam line and in the radiators.
TRAPS
Traps are used for draining the condensate from radiators, steam
piping systems, kitchen equipment, laundry equipment, hospital equip-
ment, drying equipment and many other kinds of apparatus. The usual
functions of a trap are to allow the passage of condensate and to prevent the
passage of steam. In addition to these functions, traps are frequently
required to allow the passage of air as well as condensate. Traps are also
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CHAPTER 31 — STEAM HEATING SYSTEMS
required to allow the passage of air and to prevent the passage of either
water or steam, or both.
In addition, traps are used for returning condensate either by gravity,
by steam pressure, or by both, to a boiler or other point of disposal, and
for lifting condensate from a lower to a higher elevation, or for handling
condensate from a lower to a higher pressure.
The fundamental principle upon which the operation of practically all
traps depends is that the pressure within the trap at the time of discharge
shall be equal to, or slightly in excess of, the pressure against which the
trap must discharge, including the friction head, velocity head and static
head on the discharge side of the trap. If the static head is in favor of
the trap discharge it is a minus quantity and may be deducted from the
other factors of the discharge head.
Traps may be classified according to the principle of operation as (1)
float, (2) bucket, (3) thermostatic, or (4) tilting traps.
Float Traps. A discharge valve is operated by the rise and fall of a float due to the
change of water level in the trap. When the trap is empty the float is in its lowest
position, and the discharge valve is closed. A gage glass indicates the height of water
in the chamber.
Unless float traps are well made and proportioned there is danger of considerable
steam leakage through the discharge valve due to unequal expansion of the valve and
seat and the sticking of moving parts. The discharge from a float trap is usually con-
tinuous since the height of the float, and consequently the area of the outlet, is propor-
tional to the amount of water present.
Bucket Traps. Bucket traps are of two types, the upright and inverted, and although
they are both of the open float construction, their operating principle is entirely different.
In the upright bucket trap, the water of condensation enters the trap and fills the space
between the bucket and the walls of the trap. This causes the bucket to float and forces
the valve against its seat, the valve and its stem usually being fastened to the bucket.
When the water rises above the edges of the bucket it flows into it and causes it to sink,
thereby withdrawing the valve from its seat. This permits the steam pressure acting
on the surface of the water in the bucket to force the water to a discharge opening. When
the bucket is emptied it rises and closes the valve and another cycle begins. The discharge
from this type of trap is intermittent.
In the inverted bucket trap, steam floats the inverted submerged bucket and closes the
valve. Water entering the trap fills the bucket which sinks and through compound
leverage opens the valve, and the trap discharges. It is impossible to install a water
gage glass on an inverted bucket trap, but if visual inspection is necessary, a gage glass
can be placed on the line leading to the trap. No air relief cocks can be used, but this is
unnecessary, as the elimination of air is automatically taken care of by air passing through
the vent in the top of the inverted bucket regardless of temperature.
Thermostatic Traps. Thermostatic traps are of two types, those in which the discharge
valve is operated by the relative expansion of metals, and those in which the action of
a volatile liquid is utilized for this purpose. Thermostatic traps of large capacity for
draining blast coils or very large radiators are called blast traps.
Tilting Traps. With this type of trap, water enters a bowl and rises until its weight
overbalances that of a counter-weight, and the bowl sinks to the bottom. As the bowl
sinks, a valve is opened thus admitting live steam pressure on the surface of the water
and the trap then discharges. After the water is discharged, the counter- weight sinks
and raises the bowl, which in turn closes the valve and the cycle begins again* Tilting
traps are necessarily intermittent in operation. They are not ordinarily equipped with
glass water gages, as the action of the trap shows when it is filling or emptying. The air
relief of tilting traps is taken care of by the valves of the trap.
Thermostatic traps are generally used for draining radiators and
heaters, except for very large capacities where bucket, float or blast-type
thermostatic traps are used. Thermostatic traps for this service usually
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
pass both condensate and air and in the case of float and upright bucket
traps the air is usually relieved through an auxiliary thermostatic trap in
a by-pass around the main trap. Sometimes this auxiliary air trap is an
integral part of the trap.
Blast-type thermostatic traps are sometimes used on vacuum heating
systems for connecting old one- or two-pipe gravity systems in parallel
with vacuum return line systems, in which case the blast-type thermo-
static traps should not be provided with auxiliary air by-pass, as the
action of this will allow the vacuum to draw air into the old system
through its air valves, especially when the steam is wholly or partially
Connection io Main
Vacuum Return
FIG. 20.
High Press
* Trap
METHOD OF DISCHARGING HIGH-PRESSURE APPARATUS INTO LOW-PRESSURE
HEATING MAINS AND VACUUM RETURN MAINS THROUGH
A LOW-PRESSURE TRAP
cut off. The air from the returns of such old systems should be relieved
just ahead of the traps by means of quick-venting automatic air valves,
preferably of the non-return type, especially if the other air valves on
the old system are non-return valves.
Tilting traps used for discharging to a higher or a lower pressure are
provided with two or three valves operated by the action of the trap.
In the case of the two-valve tilting traps, one valve closes a steam inlet
and the other valve opens a vent outlet while the trap is filling, and as
soon as the trap dumps, the first valve opens the steam inlet and the
second valve closes the vent outlet, while the trap discharges. In this
type of trap there must be a swinging check-valve on each side of the
trap, in addition to the usual by-pass, to prevent the pressure in the trap,
while discharging, from backing up through the inlet and the pressure
in the discharge line from backing up into the trap while it is filling. This
type of trap will blow steam out through the vent while filling, if the
pressure on the inlet side is sufficient, and should not be used, therefore,
with such pressures unless the vent is properly piped back into the return
to a feed water heater, a condenser or a perforated pipe in the bottom
of the receiver to which the trap discharges in such a way as to prevent
the escape of the steam that comes in with the condensate and passes
through the vent. In the three-valve traps of this type there is an extra
valve for closing the discharge while the trap is filling.
High pressure traps should not discharge directly into a vacuum return
522
CHAPTER 31 — STEAM HEATING SYSTEMS
Returns-.,
Check Valve, Tee.,
Gorge,
Glass
•C dir Valvt
•Safety Valve -h Wvs+e
Connection for
FIG. 21. RETURN TRAP AND RECEIVER FOR AUTOMATIC BOILER FEED
because of the vapor formed by the re-evaporation of a part of the hot
condensation. Fig. 20 shows a method which may be used for disposing of
the greater part of the vapor of re-evaporation.
Automatic Return Traps
In the general heating plant, where thermostatic traps are installed on
the heating units, it becomes necessary to provide a means for returning
the water of condensation to the boiler, if a condensation or vacuum pump
is not used. When the return main can be kept sufficiently high above the
boiler water line for all operating conditions, the water of condensation
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
will flow back by gravity, and no mechanical device is required. But
actually this does not work out in practice. It follows, therefore, that a
direct return trap is needed for the handling of the condensation even
though it may not be called into action except under some operating
condition where the pressure differential exceeds the static head provided.
The installation of a direct return trap assures safety for such systems,
and guarantees the operation of the plant under varying conditions.
Automatic return traps, sometimes called alternating receivers, may
be of the counterbalanced, tilting type, or spring actuated. These consist
of a small receiver with an internal float, and when the condensate will
not flow into the boiler under pressure, it will feed into the receiver of the
trap, and in so doing, raise or tilt the float or mechanism which actuates a
steam valve automatically. This admits steam to the receiver, at boiler
pressure, and the equalizing of the pressures which follows allows the
water to flow into the boiler. Fig. 21 shows a direct return tilting trap
and receiver properly connected for automatically feeding a boiler from a
system of returns delivering the condensate to the receiver.
PROBLEMS IN PRACTICE
1 • To what main features does the gravity one-pipe steam system owe its
popularity?
To its low cost of installation and to its simplicity.
2 • How many types of common mechanical returns are there and what are
they?
Three: (1) the mechanical return trap, (2) the condensation return pump, and (3)
the vacuum pump.
3 • In the ordinary vacuum system of steam heating, where does ihe vacuum
usually exist?
On the return side of the system only, between the radiator trap and the vacuum pump.
If the radiator supply valve is closed off, the vacuum may extend back through the
radiator as far as the supply valve; if an adequate supply of steam is furnished to the
system, some vacuum may be developed in the steam main, but neither of these can be
termed normal operation.
4 • What is the distinction between the open and the closed vapor systems?
The open vapor system has the return line always open to the atmosphere, while the
closed vapor system has an automatic device on the air vent so that air once expelled
from the system through the vent cannot re-enter via this route.
5 • On a vacuum system, what device must be placed on all drips before they
enter the vacuum return line?
A thermostatlc drip trap or occasionally, where large volumes of condensation are to be
handled, a float trap.
6 • How does the sub-atmospheric system differ in operation from the ordinary
vacuum system?
The ordinary vacuum system has pressure in the steam line, and a vacuum produced by
the vacuum pump in the return line, usually varying between 5 and 10 in. of water. The
sub-atmospheric system may have either a vacuum or pressure on the steam and return
524
CHAPTER 31 — STEAM HEATING SYSTEMS
lines, but a constant difference in pressure is maintained between the lines regardless of
what pressure or vacuum may be carried. The vacuum, which is generally produced
by condensation in the system under conditions of throttled steam supply, may run
much higher than in the ordinary vacuum systems.
7 • What is generally understood by zoning in building steam heating systems?
Zoning is a term applied to the placing of certain sections of a building on a single
temperature control instead of having either individual room control or a single tempera-
ture control governing the whole building. Zones may be horizontal, such as a single
story, a basement, or an attic, or vertical such as the north side, or the west side.
8 • Why does the water line in the far end of a wet return in a gravity steam
system rise higher than the water line in the boiler?
The friction of the steam flowing through the steam main from the boiler to the far
end of the system causes a drop in steam pressure at the point where the wet return is
connected ; consequently, the steam pressure on top of the water in the wet return is less
than the steam pressure on top of the water in the boiler, so the water in the end of the
wet return rises until a balanced condition is set up.
9 • On gravity one-pipe systems as indicated in Fig. 1 and Fig. 3, why is the
drip on the steam runout connected to wet return?
Because if it were connected to dry return, the pressure drops to two different points
would not necessarily be the same and the system would short circuit.
10 • Why cannot graduated valves be used on a one-pipe system?
Partial opening of valves would restrict flow to such an extent that the radiator could not
drain properly and would fill with water.
11 • What advantage is there to an air valve with a check to prevent the re-
entrance of expelled air?
A system equipped with such valves builds up a vacuum and holds the heat longer.
With proper controls on the boiler, lower radiator temperatures can be maintained in
mild weather, giving better plant efficiency.
12 • With a one-pipe steam heating plant designed for a total pressure drop of
J4 Ib with a check valve on the return, how high must the lowest part of the
steam main be aboye the boiler water line?
Water line difference (Ji X 28) 7 in.
Flow head required 3 in.
Friction head of check valve 4 in.
Factor of safety 6 in.
Total required 20 in,
13 • What are the essentials of a two-pipe closed vapor system?
Packless graduated valves on radiators ; thermostatic return traps on returns and drips ;
an automatic return trap to prevent water from backing out of the boiler.
14 • Why must the automatic return trap on two-pipe vapor systems be about
18 in. above the boiler water line?
That height is necessary to overcome water line difference owing to pressure drop and
friction in pipe and fittings.
15 • What is the difference between the systems illustrated in Fig. 10 and
Fig. 13?
The risers and the air eliminator in Fig, 13 are vented to atmosphere.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
16 • What is the difference between a vacuum pump and a condensation return
pump?
The vacuum pump produces and maintains a vacuum in the return lines whereas the
condensation return pump returns the condensation back to the boiler. The relation of
the boiler to the heating units is such that the condensate will not return by gravity.
17 • What is the function of a trap?
The usual function is to allow the passage of condensate and air and to prevent the
passage of steam.
18 • Under what conditions is it advisable to use a combination float and
thermostatic trap?
Where unusual capacities are required, as on large mains or blast coils.
19 • Why should the discharge from high pressure traps not go directly into a
vacuum return main?
Because of its higher temperature, the high pressure condensate would immediately
flash into steam in the vacuum main and cause difficulty with the vacuum pump.
20 • What is the function of the automatic return trap?
To insure the return of condensate to the boiler when the operating condition is such that
the boiler pressure exceeds the static head on the returns.
526
Chapter 32
PIPING FOR STEAM HEATING
SYSTEMS
Flow of Steam in Pipes, Pipe Sizes, Tables Jor Pipe Sizing, Sizing
One-Pipe Gravity Air Vent Systems, Two-Pipe Gravity Air Vent
Systems, Two-Pipe Vapor Systems, Atmospheric Systems,
Vacuum Systems, Sub -Atmospheric Systems, Orifice Systems,
High Pressure Steam, Expansion in Steam and Return Lines,
Piping Connections and Details, Boiler Connections, Hartford
Return Connection
THE design of a steam heating system should be considered under four
headings, namely, (1) the details of the heating units, (2) the arrange-
ment of the general piping scheme, (3) the details of connections, and (4)
the sizing of the lines. Items 1 and 2 are covered in Chapters 30 and 31 ,.
respectively, while this chapter considers the two latter items.
The functions of piping are to supply the heating units with steam and
to remove the condensation. In some systems both the air and con-
densation are removed from the heating units by the return piping. To
accomplish this effectively, the distribution of the steam should be
efficient and equitable, without noise, and the returns should be as short
as possible. When air is handled its escape should be facilitated to the
utmost since an air-bound system will not heat properly. Condensation
takes place in a steam system not only in the heating units, but through-
out the piping system as well, and the returns also condense any steam or
vapor that may be contained. At the same time part of the condensation
may flash back into steam when the vacuum or pressure in the return is-
considerably below the steam pressure.
It is essential that steam piping systems not only distribute steam at
full load but also at partial loads, as the average winter demand is less
than half of the demand in most severe outside temperatures. Further-
more, in heating up rapidly the load on the steam main may exceed the
maximum operating load even in extreme weather, due to the necessity
of raising the temperature of the metal in the system to the steam tem-
perature. This may require more heat than would be emitted from the
system itself after it once is thoroughly heated.
STEAM FLOW
The rate of flow of dry steam or steam with a small amount of water
flowing in the same direction is in accordance with the general laws of gas
flow and is a function of the length and diameter of the pipe, the density
of the steam, and the pressure drop through the pipe. This relationship
has been established by Babcock in the following formula:
527
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
P = 0.0000000367 ( 1 4- ~p\ -^ (1)
or
W = 5220 ,
PDd*
77+^)
where
P — loss in pressure, pounds per square inch.
d — inside diameter of pipe, inches.
L ~ length of pipe, feet.
D — weight of 1 cu ft of steam.
W ~ weight of steam flowing per hour, pounds.
Example 1. How much steam will flow per hour through 100 ft of 2-in. pipe if the
initial pressure is 1.3 Ib per square inch and the pressure drop is 1 02?
Solution. P « ~ = 0.0625 Ib; d = 2.067 in. (Table 1, Chapter 34); L = 100 ft;
ID
D = 0.04038 Ib (Table 7, Chapter 1). Substituting these values in Formula 2:
V 0
J 0.0625 X 0.04038 X 2.0675
7 3^~T = 97.2 Ib per hour.
Formula 2 does not allow for entrained water in low-pressure steam,
condensation in pipe, and roughness in commercial pipe as found in
practice.
The latent heat of steam (/zfg) at atmospheric pressure (Table 7,
Chapter 1) is 970.2 Btu per pound. Inasmuch as the heat emission of an
equivalent square foot of heating surface (radiation) is 240 Btu, 1 Ib of
970 2
steam at this pressure will supply ~ . *>•• or 4.04 sq ft of equivalent heating
surface. This figure is usually taken as 4 even. In Example 1, the weight
of steam flowing per hour would therefore supply 4 X 97.2 or 388.8 sq ft
of equivalent heating surface.
PIPE SIZES
The determination of pipe sizes for steam heating depends on the
following principal factors :
1 . The initial pressure and the total pressure drop which may be allowed between the
source of supply and the end of the return system.
2. The maximum velocity of steam allowable for quiet and dependable operation of
the system.
3. The equivalent length of the run from the boiler or source of steam supply to the
farthest heating unit.
4. Unusual conditions in the building to be heated.
Initial Pressure and Pressure Drop
Theoretically there are several factors to be considered, such as initial
pressure and pressure required at the end of the line, but it is most im-
portant that (1) the total pressure drop does not exceed the initial pressure
of the system ; (2) the pressure drop is not so great as to cause excessive
velocities; (3) there is a constant initial pressure, except on systems
528
CHAPTER 32 — PIPING FOR STEAM HEATING SYSTEMS
TABLE 1. MAXIMUM ALLOWABLE CAPACITIES OF UP-FEED RISERS FOR ONE-PIPE
Low PRESSURE STEAM
Based on A. S. H. V. E* Research Laboratory Tests
PIPE SIZE
INCHRS
VELOCITY
FEET PER SECOND
PRESSURE DROP
OUNCES
PER 100 FT
CAPACITY
SgFt
Radiation
Btu per Hour
Lb
Steam per Hour
A
B
C
D
E
F
1
14.1
0.68
45
10,961
11.3
1J€
17.6
0.66
98
23,765
24.5
i«
20.0
0.66
152
36,860
38.0
2
23.0
0.57
2S8
69,840
72.0
2H
26.0
0.54
464
112,520
116.0
3
29.0
0.48
799
193,600
199.8
3H
31.0
0.44
1144
277,000
286.0
4
32.0
0.39
1520
368,000
380.0
INSTRUCTIONS FOR USING TABLE 1
1. Capacities given in Table 1 should never be exceeded on one-pipe risers.
2. Capacities are based on J<-lb condensation per square foot equivalent radiation and actual diameter
of standard pipe.
3. All pipe should be well reamed and free from constrictions. Fittings should be up to size. (See
Tables 4 and 5).
specially designed for varying initial pressures, such as the sub-atmos-
pheric, the orifice, and the vapor systems which normally operate under
partial vacuums; (4) there is sufficient difference in level, for gravity
return systems, between the lowest point on the steam main, the heating
units, and the dry return, when considered in relation to the boiler water
line.
All systems should be designed for a low initial pressure and a reason-
ably small pressure drop for two reasons : first, the present tendency in
steam heating unmistakably points toward a constant lowering of pres-
sures even to those below atmospheric; second, a system designed in this
manner will operate under higher pressures without difficulty. When a
system designed for a relatively high initial pressure and a relatively high
pressure drop is operated at a lower pressure, it is likely to be* noisy and
have poor circulation.
The total pressure drop should never exceed one-half of the initial
pressure when condensate is flowing in the same direction as the steam.
Where the condensate must flow counter to the steam, the governing
factor is the velocity permissible without interfering with the condensate
flow. Laboratory experiments limit this to the capacities given in
Tables 1 and 2 for vertical risers and in Table 3 for horizontal pipes at
varying grades.
Maximum Velocity and Reaming
The capacity of a steam pipe in any part of a steam system depends
upon the quantity of condensation present, the directipa in which the
condensate is flowing, and the pressure drop in the pipe. Where the
£29
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 2. MAXIMUM ALLOWABLE CAPACITIES OF UP-FEED RISERS FOR Two- PIPE
Low PRESSURE STEAM
Based on A. S. H. V.E. Research Laboratory Tests
PIPE SIZE
INCHES
VELOCITY
FEET PER SECOND
PRESSURE DROP
OUNCES
PER 100 FT
CAPACITY
SqFt
Radiation
Btu per Hour
Lb
Steam per Hour
A
B
C
D
E
F
%
20
40
9550
10.0
1
23
1.78
74
17,900
18.45
IJi
27
1.57
151
36,500
37.65
1J*
30
1.48
228
55,200
57.0
2
35
1.33 •
438
106,100
109.5
m
38
1.16
678
164,100
169.4
3
41
0.95
1129
273,500
282.2
3^
42
0.81
1548
375,500
387.0
4
43
0.71
2042
495,000
510.5
INSTRUCTIONS FOR USING TABLE 2
1 . The capacities given in this table should never be exceeded on two-pipe risers.
2. Capacities are based on J^-lb condensation per square foot equivalent radiation and actual diameter
of standard pipe.
3. AH pipe should be well reamed and free from constrictions.
Tables 4 and 5.)
Fittings should be up to size. (See
quantity of condensate is limited and is flowing in the same direction as
the steam, only the pressure drop need be considered. When the con-
densate must flow against the steam, even in limited quantity, the ve-
locity of the steam must not exceed limits above which the disturbance
between the steam and the counter-flowing water may produce object-
ionable sounds, such as water hammer, or may result in the retention of
water in certain parts of the system until the steam flow is reduced
sufficiently to permit the water to pass. The velocity at which such
disturbances take place is a function of (1) the pipe size, whether the pipe
runs horizontally or vertically, (2) the pitch of the pipe if it runs hori-
zontally, and (3) the quantity of condensate flowing against the steam.
Two factors of uncertainty always exist in determining the capacity of
any steam pipe. The first is variation in manufacture, which apparently
cannot be avoided and which caused an actual difference of 20 per cent in
the capacity of a 1-in. pipe in experiments carried on at the A.S.H.V.E.
Research Laboratory (Table 4). The second is the reaming of the ends of
the pipe after cutting, which, experiments indicate, might reduce the
capacity of a 1-in. pipe as much as 28.7 per cent (Table 5). All of the
capacity tables given in this chapter include a factor of safety. However,
the pipe on which Table 4 is based showed no particular defects or con-
strictions on the inside, and the factor of safety referred to does not cover
abnormal defects or constrictions nor does it cover pipe not properly
reamed.
530
CHAPTER 32 — PIPING FOR STEAM HEATING SYSTEMS
TABLE 3. COMPARATIVE CAPACITY OF STEAM LINES AT VARIOUS PITCHES'*
Pitch of Pipe in Inches per 10 Ft
PITCH OP
1
PIPE
1A IN.
1A IN.
1 IN.
IHm.
2 IN.
3 IN.
4 IN.
5 IN.
Pipe
SqFt
Rad.
3
SqFt
Rad.
?
SqFt
Rad.
"3
SqFt
Rad.
*«
SqFt
Rad.
13
SqFt
Rad.
"3
SqFt
Rad.
"3
SqFt
Rad.
•a
Size
Based
K
Based
M
Based
^
Based
S*
Based
V
Based
'>.
Based
^
Based
.
Inches
on 240
Btu
1
on 240
Btu
1
on 240
Btu
1
on 240
Btu
on 240
Btu
§
on 240
Btu
s
on 240
Btu
C3
on 240
Btu
1
H
25.0
12
30.3
14
37.3
18
40.4
19
42.5
20
46.1
21
47.5
22
49.3
23
i
45.8
12
52.6
15
63.0
17
70.0
20
75.2
22
83.0
23
87.9
25
90.2
26
ij^
104.9
18
117.2
20
133.0
23
144.5
25
154.0
27
165.0
28
172.6
29
178.2
31
ij^
142.6
18
159.0
21
181.0
23
196.5
25
209.3
27
224.0
28
234.8
30
242.6
31
2
236.0
19
263.5
20
299.5
23
325.5
25
346.5
27
371.5
28
388.4
29
401,1
30
aData from A.S.H.V.E. Research Laboratory.
Equivalent Length of Run
All tables for the flow of steam in pipes, based on pressure drop, must
allow for the friction offered by the pipe as well as for the additional
resistance of the fittings and valves. These resistances generally are
stated in terms of straight pipe; in other words, a certain fitting will
produce a drop in pressure equivalent to so many feet of straight run of
the same size of pipe. Table 6 gives the number of feet of straight pipe
usually allowed for the more common types of fittings and valves. In all
pipe sizing tables in this chapter the length of run refers to the equivalent
length of run as distinguished from the actual length of pipe in feet. The
length of run is not usually known at the outset; hence it is necessary to
assume some pipe size at the start. Such an assumption frequently is
considerably in error and a more common and practical method is to
assume the length of run and to check this assumption after the pipes are
sized. For this purpose the length of run usually is taken as double the
actual length of pipe.
TABLE 4. PER CENT DIFFERENCE IN CAPACITY FOR CARRYING STEAM AND CONDENSATE
DUE TO VARIATION OF PIPE SIZE AND SMOOTHNESS**-
MAXIMUM CONDENSATION, LB PER HOUR
Size of pipe
5* In.
lln.
Itfln.
iMIn.
Minimum.
14.00
24.89
45.42
70.50
Maximum
15.20
30.08
52.08
82.00
Per cent variation
8.6
20.8
14.7
16.3
aData from AMERICAN SOCIETY OF HEATING AND VENTILATING ENGINEERS Research Laboratory.
TABLE 5. EFFECT OF REAMING ENTRANCE TO ONE-INCH ONE-PIPE RISERS*
MAXIMUM CAPACITY
OF RISER
PER CENT
DECREASE
Reamed entrances , ...
24.7 Ib per hour
0.0
Rounded entrances
23.9 Ib per hour
3.2
Squared entrances
22.2 Ib per hour
10.1
Three wheel cutter .
19.2 Ib per hour
22.2
Single wheel cutter
17,6 Ib per hour
28.7
aData from AMERICAN SOCIETY OF HEATING AND VENTILATING ENGINEERS Research Laboratory.
531
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 6. LENGTH IN FEET OF PI?E TO BE ADDED TO ACTUAL LENGTH OF RUN —
OWING TO FITTINGS — TO OBTAIN EQUIVALENT LENGTH
SIZE OF PIPE
INCHES
ST'D. ELBOW
SIDE OUTLET
TEE
GATE VALVE
GLOBE VALVE
ANGLE VALVE
Length in Feet to be Added to Run
2
5
16
2
18
9
VA
7
20
3
25
12
3
10
26
3
33
16
3^
12
31
4
39
19
4
14
35
5
45
22
5
18
44
7
57
28
6
22
50
9
70
32
7
26
55
10
82
37
8
31
63
12
94
42
9
35
69
13
105
47
10
39
76
15
118
52
12
47
90
18
140
63
14
53
105
20
160
72
Example of length in
feet of pipe to be added
to actual length of run.
LM5TH. -
•
\ ! EQUIVALENT LEH6TH '- 19$ -0*
TABLES FOR PIPE S1ZINQ1
Factors determining the size of a steam pipe and its allowable limit of
capacity are as follows:
1. Pipe condensate flowing with steam.
2. Pipe condensate flowing against steam.
3. Pipe and radiator condensate flowing with steam.
4. Pipe and radiator condensate flowing against steam.
It is apparent that (3) and (4) are practically limited to one-pipe
systems while (1) and (2) cover all other systems.
Tables 7 and 8, worked out for determining pipe sizes, have their col-
umns lettered continuously, Columns A through L being in Table 7, and
M through EE in Table 8. In the following text, reference made to
columns will be by letter. The tables are based on the actual inside
diameters of the pipe and the condensation of ^ Ib (4 oz) of steam per
square foot of equivalent direct radiation2 (abbreviated EDR) per hour.
The drops indicated are drops in pressure per 100 ft of equivalent length
of run. The pipe is assumed to be well reamed without unusual or notice-
able defects.
iPipe size tables in this chapter have been compiled in simplified and condensed form for the convenience
of the user: at the same time all of the information contained in previous editions of THE GUIDE has been
retained. Values of pressure drops, formerly expressed in ounces, are now expressed in fractions of a pound.
aAa steam system design has materially changed in recent years so that 240 Btu no longer expresses the
heat of condensation from a square foot of radiator surface per hour, and as present day heating units have
different characteristics from older forms of radiation, it is the purpose of THE GUIDE to gradually eliminate
the empirical expression square foot of equivalent direct radiation, EDR, and to substitute a logical unit based
on the Btu, The new terms to express the equivalent of 1000 Btu (Mb), and 1000 Btu per hour (Mbh),
have been approved by the A.S.H.V.E.
CHAPTER 32 — PIPING FOR STEAM HEATING SYSTEMS
TABLE 7. STEAM PIPE CAPACITIES
Capacity Expressed in Square Feet of Equivalent Direct Radiation
(Reference to this table will be by column letter A. through L)
This table is based on pipe size data developed through the research investiga-
tions of the AMERICAN SOCIETY OF HEATING AND VENTILATING ENGINEERS.
CAPACITIES OF STEAM MAINS AND RISERS
PIPE
SIZE
IN.
DIRECTION OF CONDENSATION FLOW IN PIPE LINE
With the Steam in One-Pipe and Two-Pipe Systems
Against the Steam
Two-Pipe Only
Supply
Risers
Up-
Feed
Radiator
Valves
and
Vertical
Con-
nections
Radiator
and
Riser
Run-
outs
Vsa Ib
or
HOz
Drop
1/24 Ib
or
^Oz
Drop
Vie Ib
or
1 Oz
Drop
Hlo
or
20z
Drop
Mlb
or
40z
Drop
>Ub
or
8 Oz
Drop
Vertical
Hori-
zontal
A
B
C
D
E
P
G
#a
fc
/b
K
Lc
H
1
IX
iy*
2
m
3^
4
5
6
8
10
12
16
30
56
122
190
386
635
1,163
1,737
2,457
4,546
7,462
15,533
28,345
45,492
84,849
~jg
173
269
546
898
1,645
2,457
3,475
6,429
10,553
21,967
40,085
64,336
121,012
30
56
122
190
386
635
1,129
1,548
2,042
"""26
58
95
195
395
700
1,150
1,700
3,150
25
45
98
152
288
464
799
1,144
1,520
39
87
134
273
449
822
1,228
1,738
3,214
5,276
10,983
20,043
32,168
60,506
46
100
155
315
518
948
1,419
2,011
3,712
6,094
12,682
23,144
37,145
69,671
111
245
380
771
1,270
2,326
3,474
4,914
9,092
14,924
31,066
56,689
90,985
169,698
157
346
538
1,091
1,797
3,289
4,913
6,950
12,858
21,105
43,934
80,171
128,672
242,024
20
55
81
165
20
55
81
165
260
475
745
1,110
2,180
All Horizontal Mains and Down-Feed Risers
3*1
Feed
Risers
Mains
and Un-
dripped
Run-
outs
Up-
Fe£
Risers
Radiator
Con-
nections
Run-
outs
Not
Dripped
SPECIAL CAPACITIES FOR
te. — All drops shown are in pounds per 100 ft of equivalent run — based on pipe properly reamed.
aDo not use Column H for drops of 1/24 or 1/32 Ib; substitute Column C or Column B as required,
bDo not use Column J for drop of 1/32 Ib except on sizes 3 in. and over; below 3 in. substitute Column B.
cOn radiator runouts over 8 ft long increase one pipe size over that shown in Table 7.
^ ~s*^+ I AMERICAN SOCIETY OF HEATING AND VENTILATING ENGINEERS ) Not to be Reprinted With-
Copyright | Heaiin{Jt Piping and Air Cmdtiiming Cmtractns Naticmd Astutoion $ out Special Permission
Table 7 may be used for sizing piping for steam heating systems by
determining the allowable or desired pressure drop per 100 equivalent
feet of run and reading from the column for that particular pressure drop.
This applies to all steam mains on both one-pipe and two-pipe systems,
vapor systems, and vacuum systems. Columns B to G, inclusive, are used
where the steam and condensation flow in the same direction, while
Columns H and / are for cases where the steam and condensation flow in
opposite directions, as in risers and runouts that are not dripped. Columns
J, K, and L are for one-pipe systems and cover riser, radiator valve, and
vertical connection sizes, and radiator and runout sizes, all of which are
based on the critical velocities of the steam to permit the counter flow of
condensation without noise.
Sizing of return piping may be done with the aid of Table 8 where pipe
capacities for wet, dry, and vacuum return lines are shown for the pressure
drops per 100 ft corresponding to the drops in Table 7. It is customary to
use the same pressure drop on both the steam and return sides of a system.
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
.t
»!
^S
T-H-rHCOtOTHOOO^OCMOM
S|8
SCS c<J O O O O
vO *H O LO O O
rH CN -^ O\ CM
O O O O O O
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-
S IO CN CO ID CSJ CO
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oc
00
534
ON co co co O\ CN CN I-H CO ^H
||
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§88888?
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^-tfOiOOOcot^-^O
•rH TH CO LO
ss?
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§31
i?
II
I
a
CHAPTER 32 — PIPING FOR STEAM HEATING SYSTEMS
Example 2. What pressure drop should be used for the steam piping of a system if
the measured length of the longest run is 500 ft and the initial pressure is not to be over
2-lb gage?
Solution. It will be assumed, if the measured lengtn of the longest run is 500 ft, that
when the allowance for fittings is added the equivalent length of run will not exceed
1,000 ft. Then, with the pressure drop not over one half of the initial pressure, the drop
could be 1 Ib or less. With a pressure drop of 1 Ib and a length of run of 1,000 ft, the
drop per 100 ft would be J-f 0 Ib, while if the total drop were 1A Ib, the drop per 100 ft
would be 3^o Ib. In the first instance the pipe could be sized according to Column D for
He Ib per 100 ft, and in the second case, the pipe could be sized according to Column C
for J^4 Ib. On completion of the sizing, the drop could be checked by taking the longest
line and actually calculating the equivalent length of run from the pipe sizes determined.
If the calculated drop is less than that assumed, the pipe size is all right; if it is more, it is
probable that there are an unusual number of fittings involved, and either the lines must
be straightened or the column for the next lower drop must be used and the lines resized.
Ordinarily resizing will be unnecessary.
. ONE-PIPE GRAVITY AIR-VENT SYSTEMS
One-pipe gravity air-vent systems in which the equivalent length of run
does not exceed 200 ft should be sized as follows :
1. For the steam main and dripped runouts to risers where the steam and condensate
flow in the same direction, use Jie-lb drop (Column D}.
2. Where the riser runouts are not dripped and the steam and condensation flow in
opposite directions, and also in the radiator runouts where the same condition occurs, use
Column L.
3. For up-feed steam risers carrying condensation back from theradiators, use Column /.
4. For dawn-feed systems the main risers of which do not carry any radiator con-
densation, use Column H.
5. For the radiator valve size and the st^^b connection, use Column X.
6. For the dry return main, use Column U.
7. For the ivet return main use Column T.
On systems exceeding an equivalent length of 200 ft, it is suggested that
the total drop be not over ^ Ib. The return piping sizes should correspond
with the drop used on the steam side of the system. Thus, where ^44b
drop is being used, the steam main and dripped runouts would be sized from
Column C; radiator runouts and undripped riser runouts from Column L;
up-feed risers from Column J; the main riser on a down-feed system from
Column C (it will be noted that if Column H is used the drop would
•exceed the limit of J^4 Ib) ; the dry return from Column R; and the wet
return from Column Q.
With a J^2-lb drop the sizing would be the same as for H* Ib except that
the steam main and dripped runouts would be sized from Column B, the
main riser on a down-feed system from Column B, the dry return from
Column 0, and the wet return from Column N.
Example 8, Size the one-pipe gravity steam system shown in Fig. 1 assuming that
this is all there is to the system or that the riser and run shown involve the longest run
on the system.
Solution. The total length of run actually shown is 215 ft. If the equivalent length
of run is taken at double this, it will amount to 430 ft, and with a total drop of J4 Ib
the drop per 100 ft will be slightly less than He Ib. It would be well in this case to use
3^24 Ib, and this would result in the theoretical sizes indicated in Table 9, These theo-
535
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 9.
PIPE SIZES FOR ONE-PIPE UP-FEED SYSTEM SHOWN
IN FIG. 1
PART OF SYSTEM
SECTION
OP PIPE
RADIATION
SUPPLIED
(Sq FT)
THEORETICAL
PIPE SIZE
(INCHES)
PRACTICAL
PIPE SIZE
(INCHES)
Branches to radiators-
Branches to radiators..
Riser
a to &
100
50
200
2
llA
2
2
Ui
2
Riser
b to c
300
2^
21A
Riser ..
c to d
400
2H
2M
Riser
d to e
500
3
3
Riser
etof
600
3
3
Branch to riser
/to £
600
3^2
3M
Supply main
J ^ 5
g to h
600
3
3
Branch to supply main
Dry return main
htoj
ftok
600
600
2H
11A
3
2
Wet return main
ktom
600
1
2
Wet return main
Wet return main
m to n
n to p
600
'600
1
i
2
2
FIG. 1. RISER, SUPPLY
MAIN AND RETURN MAIN
OF ONE- PIPE SYSTEM
retical sizes, however, should be modified by not using a wet return less than 2 in. while
the main supply, g-h, if from the uptake of a boiler, should be made the full size of the
main, or 3 in. Also the portion of the main k-m should be made 2 in. if the wet return
is made 2 in.
Notes on Gravity One- Pipe Air- Vent Systems
1. Radiator runouts over 8 ft long should be increased one pipe size.
2. Pitch of mains should be not less than % in. in 10 ft.
3. Pitch of horizontal runouts to risers and radiators should not be less than J-£ in.
in 10 ft.
4. In general, it is not desirable to have a main less than 2 in. The diameter of the
far end of the supply main should be not less than half its diameter at its largest part.
5. Supply mains, branches to risers, or risers, should be dripped where necessary.
TWO-PIPE GRAVITY AIR-VENT SYSTEMS
The method employed in determining pipe sizes for two-pipe gravity
air-vent systems is similar to that described for one-pipe systems except
that the steam mains never carry radiator condensation. The drop
allowable per 100 ft of equivalent run is obtained by taking the equiva-
lent length to the farthest radiator as double the actual distance, and
then dividing the allowable or desired total drop by the number of
hundreds of feet in the equivalent length. Thus in a system measuring
400 ft from the boiler to the farthest radiator, the approximate equivalent
length of run would be 800 ft- With a total drop of J^ Ib the drop per
100 ft would be ~ or ^6 Ib; therefore, Column D would be used for all
o
steam mains where the condensation ,and steam flow in the same direc-
tion. If a total drop of % Ib is desired, the drop per 100 ft would be ^2 Ib
536
CHAPTER 32 — PIPING FOR STEAM HEATING SYSTEMS
and Column JB would be used. If the total drop were to be 1 Ib, the drop
per 100 ft would be ^ Ib and Column E would be used.
For mains and riser runouts that are not dripped, and for radiator
runouts where in all three cases the condensation and steam flow in
opposite directions, Column I should be used, while for the steam risers
Column H should be used unless the drop per 100 ft is $$4 Ib or ^ Ib,
when Columns B or C should be substituted so as not to exceed the drop
permitted.
On an overhead down-feed system the main steam riser should be
sized by reference to Column H, but the down-feed steam risers sup-
plying the radiators should be sized by the appropriate Columns B through
G, since the condensation flows downward with the steam through them.
The riser runouts, if pitched down toward the riser as they should be, are
sized the same as the steam mains, and the radiator runouts are made the
same as in an up-feed system.
In either up-feed or down-feed systems the returns are sized in the
same manner and on the same pressure drop basis as the steam main ; the
return mains are taken from Columns 0, R, U, X, or AA according to the
drop used for the steam main; and the risers are sized by reading the
lower part of Table 8 under the column used for the mains. The hori-
zontal runouts from the riser to the radiator are not usually increased on
the return lines although there is nothing incorrect in this practice. The
same notes apply that are given for one-pipe gravity systems.
TWO-PIPE VAPOR SYSTEMS
While many manufacturers of patented vapor heating accessories have
their own schedules for pipe sizing, an inspection of these sizing tables
indicates that in general as small a drop as possible is recommended. The
reasons for this are: (1) to have the condensation return to the boiler by
gravity, (2) to obtain a more uniform distribution of steam throughout
the system, (3) because with large variation in pressure the value of
graduated valves on radiators is destroyed.
For small vapor systems where the equivalent length of run does not
exceed 200 ft, it is recommended that the main and any runouts to risers
that may be dripped should be sized from Column D, while riser runouts
not dripped and radiator runouts should employ Column /. The up-feed
steam risers should be taken from Column H. On the returns, the risers
should be sized from Column U (lower portion) and the mains from
Column U (upper portion). It should again be noted that the pressure
drop in the steam side of the system is kept the same as on the return side
except where the flow in the riser is concerned.
On a down-feed system the main vertical riser should be sized from
Column J?, but the down-feed risers can be taken from Column D al-
though it so happens that the values in Columns D and H correspond.
This will not hold true in larger systems.
For vapor systems over 200 ft of equivalent length, the drop should not
§xceed ^ Ib to J^ Ib, if possible. Thus, for a 400 ft equivalent run the
drop per 100 ft shoulcj be not over J/g Ib divided by 4, or % Ib. In this
case the steam mains would be sized from Column B ; the radiator and
undripped riser runouts from Column I; the risers from Column B,
537
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
because Column H gives a drop in excess of 5^ lb. On a down-feed
system, Column B would have to be used for both the main riser and the
smaller risers feeding the radiators in order not to increase the drop over
J^2 Ib- The return risers would be sized from the lower portion of Column
0 and the dry return main from the upper portion of the same column,
while any wet returns would be sized from Column N. The same pressure
drop is applied on both the steam and the return sides of the system.
Notes on Vapor 'Systems
1. Radiator runouts over 8 ft long should be increased one pipe size.
2. Pitch of mains should be not less than y% in. in 10 ft.
3. Pitch of horizontal runouts to risers and radiators should be not less than 1A in.
in 10 ft.
4. In general it is not desirable to have a supply main smaller than 2 in., and when the
supply main is 3 in. or over at the boiler or pressure reducing valve it should be not less
than 2 J^ in. at the far end.
5. When necessary, supply main, supply risers, or branches to supply risers should be
dripped separately into a wet return. The drip for a vapor system may be connected
into the dry return through a thermostatic drip trap.
VACUUM SYSTEMS
Vacuum systems are usually employed in large installations and have
total drops varying from J^ to J^ Ib. Systems where the maximum
equivalent length does not exceed 200 ft preferably employ the smaller
pressure drop while systems over 200 ft equivalent length of run more
frequently go to the higher drop, owing to the relatively greater saving in
pipe sizes. For example, a system with 1200 ft longest equivalent length
of run would employ a drop per 100 ft of J^ Ib divided by 12, or J^4 Ib.
In this case the steam main would be sized from Column C, and the risers
also from Column C (Column H could be used as far as critical velocity is
concerned but the drop would exceed the limit of J^4 Ib). Riser runouts,
if dripped, would use Column C but if undripped would use Column I;
radiator runouts, Column I; return risers, lower part of Column S;
return runouts to radiators, one pipe size larger than the radiator trap
connections.
Notes on Vacuum Systems
1. It is not generally considered good practice to exceed J^-lb drop per 100 ft of
-equivalent run nor to exceed 1 Ib total pressure drop in any system.
2. Radiator runouts over 8 ft long should be increased one pipe size.
3. Pitch of mains should be not less than Y% in, in 10 ft.
4. Pitch of horizontal runouts to risers and radiators should be not less than }^ in.
in 10 ft.
5. In general it is not considered desirable to have a supply main smaller than 2 in.
When the supply main is 3 in. or over, at the boiler or pressure reducing valve, it should
be not less than 2 J^ in. at the far end.
6. When necessary, the supply main, supply riser, or branch to a supply riser should
be dripped separately through a thermostatic trap into the vacuum return. A connec-
tion should not be made between the steam and return sides of a vacuum system withoftt
interposing a thermostatic trap to prevent the steam from entering the return line.
7. Lifts should be avoided if possible, but when they cannot be eliminated they
should be made in the manner described in Chapter 31 under Up- Feed Vacuum Systems.
538
CHAPTER 32 — PIPING FOR STEAM HEATING SYSTEMS
ATMOSPHERIC SYSTEMS
The sizing of the supply and return piping on atmospheric systems is
practically identical with the sizing used for vacuum systems and the
same notes apply, except that no lift can be made in the return line.
SUB-ATMOSPHERIC SYSTEMS
Any properly pitched, correctly sized vacuum system without a lift
may be used as a sub-atmospheric system when the proper equipment is
substituted for the ordinary vacuum pump, traps, and controls. On new
systems manufacturers usually recommend a drop on the steam line of
between J^ and Y% Ib for the total run, and suggest adding 25 ft to the
total equivalent length of run to insure that the steam gets through to the
last radiator.
The same notes apply to these systems as for vacuum systems, except
that no lifts can be made in the returns.
ORIFICE SYSTEMS
The orifice systems can be operated with any piping system suitable
for vacuum operation, according to experienced designers. Because these
systems vary considerably in detail, it is advisable to consult the manu-
facturer of the particular system contemplated for recommendations.
The same notes apply to these systems as to vacuum systems, except
that lifts cannot be made in the returns of orifice systems if a vacuum
pump is used.
HIGH PRESSURE STEAM
When steam heating systems are supplied with steam from a high
pressure plant, one or more pressure-reducing valves are used to bring the
pressure down to that required by the heating system. It has been con-
sidered good practice to make the pressure reductions in steps not to
exceed 50 Ib in each case. For example, in reducing from 100-lb gage to
2-lb gage, two pressure reducing valves would be used, the first reducing
the pressure from 100-lb gage to 50 Ib and the second reducing the pressure
from 50-lb gage to 2-lb gage. Valves are available that will reduce 100 Ib
in one step, and it is questionable whether two valves are now required
for initial pressures of 150 Ib or less.
The pressure-reducing valve, or pressure-regulator as it is sometimes
termed, has ratings which vary 200 to 400 per cent. Some of these
ratings are based on arbitrary steam velocities through the valve of
5,000 to 10,000 fpm and it is assumed that the valve when wide open has
the same area as the pipe on the inlet opening of the. valve. It is well
known that steam flowing through an orifice increases its velocity until
the pressure on the outlet side is reduced to 58 per cent of the absolute
pressure on the inlet side, and that with further reduction of pressure on
the outlet side little change in velocity will be obtained. As practically
all pressure-reducing valves used for steam heating work lower the steam
pressure to less than 58 per cent of the inlet pressures, only the maximum
velocity through such valves need be considered. If it is assumed that
the valve, when fully open, has an area equal to that of the inlet pipe size,
539
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 10. CAPACITIES OF PRESSURE-REDUCING VALVES
(100-LB GAGE DOWN TO ANY PRESSURE — 52 LB OR LESS)
INLET NOMINAL
PIPE DIAMETER
(INCHES)
POTTNDS STEAM
PER HOXTR
AT 100-Ln GAGE
EQUIVALENT DIRECT
RADIATION SQ FT
AT MLB
EQUIVALENT DIRECT
RADIATION SQ FT
AT 1/3 LB
1A
866
3,464
2,598
%
1,576
6,304
4,728
2,459
9,836
7,377
Ui
4,263
17,052
12,689
1H
5,808
23,232
17,424
2
9,564
38,256
28,692
2^
13,623
54,492
40,869
3
21,041
84,104
63,123
&A
28,213
112,852
84,039
4
36,285
145,140
108,855
5
56,971
227,884
170,913
6
82,336
329,344
247,008
Formula:
where
- = pounds per hour passed by orifice.
.4 = area of inlet pipe, square inches.
V — velocity of steam through orifice (approximately 870 fps).
50 ~ 70 per cent efficiency of orifice less 20 per cent for factor of safety,
144 = square inches in 1 sq ft.
3600 = seconds in one hour.
3.8 » cubic feet per pound at 100-lb gage.
that the steam is flowing into a pressure less than 58 per cent of the initial
pressure, that the orifice efficiency is approximately 70 per cent, and that
20 per cent more is allowed for a factor of safety, then the pressure
reducing valves will have the working capacities shown in Table 10. If
the valve, when fully open, does not give an orifice area equal to that of
the pipe on the inlet side, then the capacities will be proportional to the
percentage of opening secured, taking the pipe area as 100 per cent.
Most exact regulation of pressure on steam heating systems is secured
from diaphragm-operated valves controlled by a pilot line from the low
pressure pipe, taken off the low pressure main: at least 15 ft from the
reducing valve. The reducing valves operating on the proportional-
reduction principle will give a variation of steam pressure on the low
pressure side if the initial pressure varies between considerable limits.
The so-called dead-end valve is used for reduced pressures where the line
has not sufficient condensing capacity at all times to condense the leakage
that might occur with the ordinary valve. Single-disc valves do not give
as close regulation as double-disc valves, but the single disc is preferable
where dead-end valves are necessary, such as on short runs to thermo-
statically controlled hot water heaters, central fan heating units and
unit heaters.
The correct installation (Fig. 2) of a pressure-reducing valve includes
a pressure-reducing valve with a gate valve on each side, a by-pass con-
trolled by a globe valve, a pressure gage on the low pressure side, and a
safety valve on the low pressure main at some point, usually within a
reasonable distance of the pressure-reducing valve. Pressure-reducing
valves should have expanded outlets for sizes greater than 2 in. Where
the steam main is of still larger diameter than the expanded outlet, and in
540
CHAPTER 32 — PIPING FOR STEAM HEATING SYSTEMS
cases where straight valves are used, an increaser is placed close against
the outlet of the valve to reduce the velocity immediately after passing
through the valve. Strainers are recommended on the inlets of all
pressure-reducing valves. A pressure gage may be located on the high-
pressure line near the valve if desired.
Owing to the large variation in steam demand on the average heating
system, it is generally advisable to use two pressure-reducing valves con-
nected in parallel. One valve should be large enough for the maximum
load and the other should have a diameter approximately half that of the
first. The smaller valve can be used most of the time, for it will give
much better regulation than the larger one on light or normal loads.
Less trouble from expansion leaks will occur when the bypass
valve is on the same center line as the pressure reducing valve
Bypass (same size as high fc-^Globe valve
pressure supply line) N
Pressure gage^ jj Gate valve U /Pressure gage
if desired
.. f „ ^^,^,, ... Low pressure steam
High pressure Steam
Drjp' strainer / i Gate valve
Pressure reducing valve x Pilot line
FIG. 2. TYPICAL PRESSURE-REDUCING VALVE INSTALLATION
Control Valves
Gate valves are recommended in all cases where service demands that
the valve be either entirely open or entirely closed, but they should never
be used for throttling. Angle globe valves and straight globe valves
should be used for throttling, as done on by-passes around pressure
reducing valves or on by-passes around traps.
EXPANSION IN STEAM AND RETURN LINES
Because all steam and return lines expand and contract with changes
in temperature, provision should be made for such movement. The
expansion in steam supply pipes is normally taken at 1J^ to 1^ in. per
100 ft and in return lines at one-half or two-thirds of this amount. It
may be calculated accurately if the temperature rise and fall can be
determined with reasonable certainty (Page 586, Chapter 34). The tem-
perature at the time of erection often has a greater expansion effect on
piping than the temperature in the building after it has been put into
service.
Expansion may be taken care of by any, or all, of three different
methods, namely, (1) the spring in the pipe including offsets and expan-
sion bends, (2) the turning of the pipe on its threads and swing joints, and
(3) the use of expansion joints.
By the first scheme, which is the most popular method where space
permits, the pipe is offset, or broken, around rooms or corners, and is hung
so that the spring in the pipe at right angles to the expansion movement
is sufficient to absorb the expansion* If conditions do not lend themselves
to this treatment, regular expansion bends of the U or offset type may be
used. In tight places such as pipe tunnels the expansion joint is pre-
ferable.
541
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
On riser runouts and radiator runouts the swing joint is used almost
without exception. On high vertical risers the pipes may be reversed
every five to ten stories; that is, the supply is carried over to the adjacent
return riser location and the return riser is run over to the former supply
riser location, thus making horizontal offsets in each line. Corrugated
copper expansion joints also are used on risers but must be made acces-
sible in case future replacement becomes necessary.
EXPANSION BENDS
The calculation of the distance required for offsets and the size of
expansion bends necessary to absorb a given amount of expansion leads
into complicated formulae and is a subject of controversy. It seems to
have been demonstrated, however, that the shape of the bend, the radius
used, the relative amounts of straight and curved pipe in a bend, and the
Fitting offset
A+B+OL
U bend with
4 fittings
Offset bend
Radial U bend
rr; -^ Circle bend
.Offset U bend
FIG. 3. MEASUREMENT OF L ON VARIOUS PIPE BENDS AND OFFSETS
FOR ABSORBING. EXPANSION
type of bend have little bearing on the amount of expansion for which
they will safely provide. The size, weight and material of the pipe and the
length of all of the pipe in the bend, or even in the offset, have a bearing
on its capacity to absorb expansion without straining the pipe material
beyond the safe working stress. In Fig. 3 typical pipe bends and offsets
for absorbing expansion are shown. The lengths L are those which are
used in determining the stress in the pipe.
Fig. 4 shows a set of curves for standard weight steel pipe bends from
which the approximate amount of pipe L (Fig. 3) for each pipe size may
be determined from the amount of expansion movement that must be
absorbed. These curves are such that the maximum fiber stress in any
part of the bend will not be over 16,000 Ib per square inch. Since 12,000
Ib per square inch is considered to be a maximum working fiber stress in
wrought iron pipe, an additional 33 J4 per cent must be added to the
length of this type of pipe.
The amount of expansion can be doubled for a bend if the bend is cold
sprung for one-half of the expansion movement. In other words, if the
bend is erected with the main pipe cut short one-half of the expected
expansion and the bend is then sprung open to meet the shortened pipe,
542
CHAPTER 32 — PIPING FOR STEAM HEATING SYSTEMS
23456
EXPANSION ABSORBED IN INCHES
FIG. 4. CURVES GIVING LENGTH L OF BEND OF OFFSET NECESSARY TO
ABSORB EXPANSION (WITHOUT COLD SPRING)
the expansion in the main will first allow the bend to go back to its neutral
point and then will compress the bend an equal distance beyond the
neutral point, thus securing a doubled capacity. Generally only a portion
of the cold spring is considered as being effective, owing to the difficulties
of erecting the bends with sufficient exactitude in the length of the main
line and the difficulty of cold springing. See additional material on pipe
expansion in Chapter 34.
PIPING CONNECTIONS AND DETAILS
Piping connections may be classified into two groups: first, those
suitable for any system of steam heating; second, those devised for certain
systems which cannot be satisfactorily applied to any other type. There
are also various details that apply to piping on the steam side which
cannot be used on the returns. An installation that is designed and sized
correctly and installed with care may be rendered defective by the use of
improper connections, such as runouts that do not allow for expansion,
thermostatic traps unprotected from scale, pressure-reducing valves
without strainers, and lack of drips at required points.
BOILER CONNECTIONS
Supply
Boiler headers and connections have the largest sizes of pipe used in a
system. Cast-iron, horizontal-type, low pressure heating boilers usually
have several tapped outlets in the top, the manufacturers recommending
their use in order to reduce the velocity of the steam in the vertical up-
takes from the boiler and to permit entrained water to return to the
boiler instead of being carried over into the steam main where it must be
cared for by dripping. Steel heating boilers usually are equipped with
only one steam outlet but many engineers believe that better results are
obtained by specifying that such boilers have two. The second outlet,
usually located 3 or 4 ft back of the regular one, reduces the velocity
5Q per cent in the steam uptake.
Fig. 5 shows a type of boiler connection that was used for many years
and one with which some boilers are now piped. The uptakes are carried
as high as possible, turned horizontally and run out to the side of the
boiler and then are connected together into the main boiler runout which
543
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
drops into the top of the boiler header through a boiler stop valve. No
drips are provided on this type of runout except a very small one which
is sometimes installed on the boiler side of the stop valve. Fig. 6 shows a
type of boiler connection which is regarded as superior to that shown in
Fig. 5 and which is the type illustrated in the system diagrams in Chapter
31. This type is similar to that shown in Fig. 5 except that the horizontal
branches from the uptakes are connected into the main boiler runout, and
the steam is carried toward the rear of the boiler. The branch to the
building or boiler header is taken off behind the last horizontal boiler con-
nection. At the rear end of this main runout, a large size drip, or balance
pipe, is dropped down into the boiler return, or into the top of the Hart-
ford Loop, which is described in a following paragraph. As a result, any
water carried over from the boiler follows the direction of steam flow
Reducing ell
\
Uptake -
Main runout to
building or
header
•Drip and balance pipe
Water line
Hartford return connection
Main wet return
FIG. 5. OLD STYLE STANDARD BOILER
CONNECTIONS
FIG. 6. APPROVED METHOD OF BOILER
CONNECTIONS
toward the rear and is discharged into the rear drip, or balance pipe,
without being carried over into the system.
Return
Cast-iron boilers are generally provided with return tappings on both
sides, but steel boilers often are equipped with only one return tapping.
A boiler with side return tappings will usually have a more effective cir-
culation if both tappings are used. Check valves generally should not be
used on the return connection to steam heating boilers because they are
not always dependable inasmuch as a small piece of scale or dirt lodged
on the seat will hold the tongue open and make the check useless. These
valves also offer a certain amount of resistance to the returns coming back
to the boiler, and in gravity systems will raise the water line in the far
end of the wet return several inches3. However, if check valves are
omitted and the steam pressure is raised with the boiler steam valve
closed, the water in the boiler will be blown out into the return system
with the accompanying danger of boiler damage. These objections are
largely overcome with the Hartford return connection.
•Sec method of calculating height above water line for gravity one-pipe systems in Chapter 31.
544
CHAPTER 32 — PIPING FOR STEAM HEATING SYSTEMS
Hartford Return Connection
In order to prevent the boiler from losing its water under any circum-
stances, the use of the Hartford Connection, or the Underwriters Loop,
is recommended. Fig. 7 shows this connection for both single boiler and
two-boiler installations. By balancing the column of water in the loop
against the steam pressure, the water cannot be blown out of the loop
whatever the relative pressure conditions in the boiler, steam lines, or
return lines. This balancing is done by raising the return to approxi-
mately the normal water line of the boiler, looping it back to the boiler
inlet and connecting the top of this loop by means of a balance pipe with
the steam runout from the boiler. It is important that this balance pipe
be connected into the boiler steam line on the boiler side of all valves.
rTHESE CONNECTIONS SHOULD &E AS SHO&T AS PRACTICAL USING AS FEW-,
\TUQNS AS POSSIBLE. THE. SIZES SHOULD PBEFECABLY BE NOT
SMALLER THAN GlVEM IN TABLE BELOW.
GfcATE AREA PIPE SIZE
4 SQ. FEET OS LESS 11//
THESE CONNECTIONS TO &E
' TAKEN OFF BETWEEN STOP
' VALVES (IF ANY) AMD BOILEfc
THESE PIPES MAY BE ANY SIZE COUSlDE&ED PHOPEa FOB I
BOILERS AWD LESS THAN STEAM CONWECTIQUS IN TABLE ABOVE."
FIG. 7. THE HARTFORD RETURN CONNECTION
Theoretically, the top of the loop should be at the normal boiler water
line but since this installation often causes trouble from water hammer in
the top of thejloop, this top is usually made 2 in. below the normal boiler
water line to keep the horizontal pipe at the top submerged under all
normal conditions. It is important that this top of the loop be made with
the shortest possible horizontal pipe, a close nipple being employed.
Sizing Boiler Connections
Little authentic information is available on the sizing of boiler runouts
and steam headers. Although many engineers prefer an enlarged steam
header to serve as additional steam storage space, there ordinarily is no
sudden demand for steam in a steam heating system except during the
heating-up period, at which time a large steam header is a disadvantage
rather than an advantage. The boiler header may be sized by first com-
puting the maximum load that must be carried by any portion of the
header under any conceivable method of operation, and then applying
the same schedule of pipe sizing to the header as is used on the steam
mains for the building. The horizontal runouts from the boiler, or boilers,
may be sized by calculating the heaviest load that will be placed on the
boiler at any time, and sizing the runout on the same basis as the building
mains. The difference in size between the vertical uptakes from the
545
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
6,000 sq ft
2,000 sq ft
LI
8,000 sq ft
8,000 sq ft
8,000 sq ft
FIG. 8. BOILER STEAM HEADER AND CONNECTIONS
boiler and the horizontal main or runout is compensated for by the use of
reducing ells (Figs. 5 and 6).
The following example illustrates the sizing of the boiler connections
shown in Fig. 8.
Example 4- Determine the size of boiler steam header and connections (Fig. 8) if
there are three boilers, two to carry 50 per cent of the load each, and the third to be used
as a spare. The steam mains are based on J^-lb drop per 100 sq ft of equivalent direct
radiation (EDR).
Solution:
Size of Boiler Header
WHEN
OPERATING
ON BOILIRS
LOAD ON VAEIOUS PORTIONS OF HEADER
MAXIMUM
LOAD
A
B
C
D
E
F
Nos. 1 and 2
Nos. 2 and 3
Nos. 3 and 1
6000
6000
6000
0
6000
0
2000
8000
2000
4000
2000
2000
3000
3000
3000
3000
3000
3000
6000
8000
6000
Max. Load
6000
6000
8000
4000
3000
3000
8000
8000 sq ft @ H lb per 100 ft * 6 in. main. (See Table 7.)
Size of Boiler Runouts
The three runouts
GI. G^t Gs
« 2667 sq ft each
«i>
4 in, pipe.
i, JSTa, H8 = 2667 sq ft each
i, /a, J* = 5333 sq ft each
i, Ki, Kt = 8000 sq ft each
£ lb per 100 ft
Jg lb per 100 f t = 4 in. pipe4 (See Table 7).
^ lb per 100 f t « 5 in. pipe4 (See Table 7),
J$ lb per 100 ft « 6 in. pipe4 (See Table 7),
The uptakes from the boiler probably would be 6 in. pipe with a 6 in. X 4 in. reducing
ell at top.
Return connections to boilers in gravity systems are made the same
size as the return main itself. Where the return is split and connected to
Wote. — As JCi, Ka, JCi all carry 8000 sq ft and are 6 in. pipe, the whole runout including Ji, /a and /*
would be made 6 in. pipe, also.
546
CHAPTER 32 — PIPING FOR STEAM HEATING SYSTEMS
two tappings on the same boiler, both connections are made the full size
of the return line. Where two or more boilers are in use, the return to
each may be sized to carry the full amount of return for the maximum load
which that boiler will be required to carry. Where two boilers are used,
one of them being a spare, the full size of the return main would be
carried to each boiler, but if three boilers are installed, with one spare, the
return line to each boiler would require only half of the capacity of the
entire system, or, if the boiler capacity were more than one-half the entire
system load, the return would be sized on the basis of the maximum
boiler capacity. As the return piping around the boiler is usually small
and short, it should not be sized to the minimum.
With returns pumped from a vacuum or receiver return pump, the size
of the line may be calculated from the water rate on the pump discharge
when it is operating, and the line sized for a very small pressure drop, the
size being obtained from the Chart for Friction Losses for Various Rates
of Flow of Water, Fig. 3, Chapter 35. The relative boiler loads should be
considered, as in the case of gravity return connections.
Radiator Connections
Radiator connections are important on account of the number of
repetitions which occur in every heating installation. They must be
properly pitched and they must be arranged to allow not only for move-
ment in the riser but, in frame buildings, for the shrinkage of the building.
In a three story building this sometimes amounts to 1 in. or more. The
simplest connection is that for the one-pipe system where only one radia-
tor connection is necessary. Where the radiator runouts are located on
the ceiling or under the floor, sufficient space usually is available to make
a good swing joint with plenty of pitch, but where the runouts must come
above the floor the vertical space is small and the runouts can project out
into the room only a short distance. Fig. 9 illustrates two satisfactory
methods of making runouts on a one-pipe gravity air vent system of
either the up-feed or down-feed type, the runout below the floor being
indicated in full lines and the runout above the floor in dotted lines.
Sometimes it is necessary to set a radiator on pedestals, or to use high
legs, in order to obtain sufficient vertical distance to accommodate above-
the-floor runouts. Particular attention must be given to the riser expan-
sion as it will raise the runout and thereby reduce the pitch.
Similar connections for a two-pipe system of the gravity air vent type
are illustrated in Fig. 10 for the old steam type radiator. If the water
type is used, the supply tapping is at the top instead of at the bottom, the
runouts otherwise remaining as shown in Fig. 10. A satisfactory type
of radiator connection for atmospheric, vapor, vacuum, sub-atmos-
pheric, and orifice systems of both the up-feed and down-feed types is
shown in Fig. 11.
While short radiators, not exceeding 8 to 10 sections, may be supplied
and returned from the same end as indicated in Fig. 12, the top-an-
bottom-opposite-end method is to be preferred in all cases where it can be
used. On down -feed systems of the atmospheric, vapor, vacuum, sub-
atmospheric, and orifice types, the bottom of the supply riser must be
dripped into the return somewhat as illustrated in Fig. 13. On up-feed
systems of the vapor and atmospheric types, where radiators in the
547
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
; VALVE
-•Runout below floor
PLAN
L
Globe
Runout valve
above
(floor i|
Hot
lyFloor
Runout below floor
ELEVATION
FIG. 9. TYPICAL ONE-PIPE RADIATOR
CONNECTIONS (UP-FEED OR DOWN-FEED)
KCENTQlC
BUSHING
FIG. 12. TOP AND BOTTOM RADIATOR
CONNECTIONS FROM UP- OR DOWN-FEED
RISERS. (NOT TO EXCEED 8 TO 10
SECTIONS.)
Note.— Suitable for up-feed or down-feed at-
mospheric, vapor, vacuum, sub-atmospheric, and
orifice systems. Opposite end connections always
preferable.
WATEQ-TYPE
/ CA01ATOQ
ECCENTQlC
^ BUSHIMG
•TUAP
-TBAP
FIG. 10. CONNECTIONS TO STEAM-TYPE
RADIATOR FOR TWO-PIPE GRAVITY
SYSTEM, UP-FEED OR DOWN-FEED
Note. — Steam-type radiators should not be used
on any except gravity one-pipe and gravity two-
pipe systems.
FIG. 13. TOP AND BOTTOM OPPOSITE END
RADIATOR CONNECTIONS WITH HEEL OF
DOWN-FEED RISER DRIPPED INTO
DRY RETURN
Note. — Suitable for down-feed only. For at-
mospheric, vapor, vacuum, sub-atmospheric, and
orifice systems.
FIG. 11. TOP AND BOTTOM OPPOSITE END
RADIATOR CONNECTIONS FROM UP
OR DOWN-FEED RISERS
Not«.t — Suitable for up-feed or down-feed at-
mospheric, vapor, vacuum, sub-atmospheric and
orifice systems.
FIG, 14. CONNECTIONS TO RADIATOR HUNG
ON WALL
Note.. — For up-feed with radiators below level
of steam main. For atmospheric and vapor systems.
JNot suitable for vacuum, sub-atmospheric, or
orifice systems.
548
CHAPTER 32 — PIPING FOR STEAM HEATING SYSTEMS
basement are located below the level of the steam main, the drop to the
radiator is dripped into the wet return and an air line is used to vent the
return radiator connection into an overhead return line, as illustrated in
Fig. 14. When the radiator stands on the floor below the main, the drip
on the steam branch down to the radiator may be omitted if an overhead
valve, as shown in Fig. 15, is used. This method is also suitable for
vacuum, sub-atmospheric, and orifice systems.
Convector Connections
Convectors often are installed without control valves, a damper being
used to shut off the flow of air to retard the heat transfer from the con-
vector even though it is still supplied with steam. The piping connec-
tions for a convector with the inlet and outlet at the same end are shown
in Fig. 16. There is no valve on the steam side but there is a thermostatic
trap on the return. The damper for control is shown immediately above
the convector. This piping is suitable for atmospheric, vapor, vacuum,
sub-atmospheric, and orifice systems of the up-feed type. A similar unit
with connections on opposite ends and suitable for the same systems is
shown in Fig. 17. This unit has no damper but requires a valve on the
steam connection for control. When valves must be located so as to be
accessible from the supply air grille, the arrangement usually takes the
form indicated in Fig. 18. Convectors with damper control, installed in
cabinets or under window sills, usually are connected as shown in Fig. 19.
A convector located in the basement and supplying air to a room on the
floor above may be piped as pictured in Fig. 20 for all, systems except
gravity one-pipe or two-pipe systems.
Vapor systems with heating units in the basement where the returns
are wet would be treated as in Fig. 21. Similar heating units where a dry
return is available would be connected as shown in Fig. 22. If the dry
return were on a vacuum, atmospheric, sub-atmospheric or orifice system,
the treatment would be identical.
Pipe Coil Connections
Pipe coils, unless coupled in a correct manner, often give trouble from
short circuiting and poor circulation. The method of connecting shown
in Fig. 23 is suitable for atmospheric, vapor, vacuum, sub-atmospheric,
and orifice systems.
Indirect Air Heater Connections
Heating units for central fan systems have simple connections on the
steam side. The steam main is carried into the fan room and has a
single branch tapped off for each row of heating units. Each of these
main branches is split into as many connections as need be made to each
row, governed by the number of stacks and the width of the stacks. Each
stack must have at least one steam connection, and wide stacks are more
evenly heated with two steam connections, one at each end.
The piping shown in Fig. 24 is for small stacks and has the steam con-
nected at only one end. On the return side all of the returns are collected
together through check valves and are passed through blast traps which
are connected to the vacuum return or to an atmospheric return. The air
549
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
550
CHAPTER 32 — PIPING FOR STEAM HEATING SYSTEMS
INDIRECT QAOATOG.
-Thermostatic trap
DBYBETUBW
'SUPPLY MAIN
FIG. 22. TYPICAL PIPING CONNECTIONS
TO INDIRECT RADIATORS WITH
DRY RETURN
Full size of tapping -
Reducing ell
"o return line
beyond blast traps
To blast trap
Check valve
Note. — Suitable for atmospheric, vapor, vacuum, FlG. 25. HEATING UNIT RETURN CON-
sub-atmospheric, and orifice systems. NECTION WITH SEPARATE AlR LlNE
Ill
1
Jt
TYPICAL CONHKTIONS TO MANIFOLD
COILS OF MOT OVEE S PPES
, e
TYPICAL CONNECTIONS TO MA.N1FOID
CO\LS HW1M6 MORE THAN 6 PPES.
FIG. 23. TYPICAL PIPE COIL CONNECTIONS
Note. — Suitable for up-feed or down-feed. For atmospheric, vapor, vacuum, sub-atmospheric, and
orifice systems.
BLAST HEATERS ,
SUPPLY AND RETURN CONNECTIONS TO BLAST COILS
FOR VACUUM SYSTEM US)H<5 BLAST TRAP OM EACH TIER,
FIG. 24, CONNECTIONS FOR HEATING
UNITS OF CENTRAL FAN SYSTEMS
•STUNNER
TBAP
FIG, 26. TYPICAL CONNECTIONS TO
CENTRAL FAN SYSTEM HEATING
UNITS EXCEEDING 12 SECTIONS
Note. — Suitable for atmospheric and vacuum Note. — Suitable for vacuum and atmospheric
systems, systems.
551
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
from the stacks, in the case illustrated, passes up into a small air line and
through a thermostatic trap into a line connecting into the return beyond
the blast trap. It is important to use a nipple the full size of the outlet
tapping on the stack and to reduce the pipe size to the normal return size
required, by the use of a reducing ell, as indicated in Fig. 25.
Where the stacks contain some thirteen or more sections, an auxiliary
air tapping is made to the lower portion of one of the middle sections, in
the manner illustrated in Fig. 26, to prevent air collecting at this point.
Thermostatic control as applied to such heating units in modern practice
"~wTr 'W\ y^: gr~"*y
Blast trap with
thermostatic
bypass
urn from lower tier
- — — — — — _ «. _ _....._
^Return from upper tier
To vacuum pump
FIG. 27. TYPICAL PIPING FOR ATMOSPHERIC AND VACUUM SYSTEMS WITH
THERMOSTATIC CONTROL (CENTRAL FAN SYSTEM)
consists of a thermostatic valve located in each main branch from the
steam line so that each valve will open or close a complete row of stacks
across the entire face of the heating unit. The stack closest to the fresh
air intake is not usually equipped with a control valve. Steam is fur-
nished continually to this coil to prevent freezing, and only the supply
pipe is equipped with a gate valve. In this case no particular attention
need be paid to the method of connecting the returns, that is, they do not
need to be connected in parallel with the steam connections but may be
hooked together in any convenient manner. The arrangement shown in
552
CHAPTER 32 — PIPING FOR STEAM HEATING SYSTEMS
Fig. 27 is satisfactory. A detail of the arrangement where a connection is
made with a stack is shown in Fig. 28. It is essential to have a check
valve on each individual stack to prevent reverse flow when the ther-
mostatic valve in the steam line closes off and a partial vacuum is pro-
duced in the stack. The end of the steam main also should be dripped as
indicated in Fig. 27.
If the separate air line is used as shown in Fig. 24, the blast traps may
be supplied without thermostatic by-passes but if the piping is arranged
as shown in Figs. 26 or 27, the blast traps must be supplied with the
thermostatic by-passes to permit the passage of the air.
PIPE SIZING FOR INDIRECT HEATING UNITS
Pipe connections and mains for indirect heating units are sized in a
manner similar to radiators, but the equivalent direct radiation must be
ascertained for each row of heating unit stacks and then must be divided
into the number of stacks constituting that row and into the number of
connections to each stack.
x 6P ><_ to_r ^ Q x fa -
55.2 X~ 240 "220.8
where
EDR
j?DR =
(3)
equivalent direct radiation, square feet.
Q = volume of air, cubic feet per minute.
/e = the temperature of the air entering the row of heating units under con-
sideration, degrees Fahrenheit.
t\ = the temperature of the air leaving the row of heating units under considera-
tion, degrees Fahrenheit.
60 = the number of minutes in one hour.
55.2 = the number of cubic feet of air heated 1 F by 1 Btu.
240 = the number of Btu in 1 sq ft of EDR.
Example 5. Assume that the heating units shown in Fig. 27 are handling 50,000 cfm
of air and that the rise in the first row is from 0 to 40 F, in the second row from 40 to
65 F, and in the third row from 65 to 80 F. What is the load in EDR on each supply
and return connection?
Solution. For row 1,
j
For row 2,
For row 3,
R
50,000 X (40 - 0) _
220.8
50,000 X (65 - 4
so
sq
"220.8
R = 50,000 X (80 - 65)
5661 sq ft.
3397 sq ft.
220.8
Each row of heating units consists of four stacks and each stack has two connections
so that the load on each stack and each connection of the stack is as follows:
Row
TOTAL LOAD
(EDR)
STACK LOAD*
(EDR)
CONNECTION LoADb
(EDR)
1
9058
2265
2265 or 1132
2
5661
1415
1415 or 708
3
3397
849
849 or 425
quarter of total row load.
bQne half of stack load if two steam connections are made; otherwise, same as stack load.
553
AMERICAN SOCIETY of HEATING drid VENTILATING ENGINEERS GUIDE, 1935
Reducing el!
To blast trap
FIG. 28. HEATING UNIT RETURN
CONNECTION WITHOUT SEPARATE
AIR LINE (CENTRAL FAN SYSTEM)
r
TO flND LENGTHC - MULTIPLY A,
BY CONSTANT FOQ ASlQLE B>.
FIG. 32, CONSTANTS FOR DETERMINING
PROPER LENGTH OF OFFSET PIPE
45° ELI
ACCEPTABLE METHOD PGSFEGED METHOD
FIG. 33. ACCEPTABLE AND PREFERRED
METHODS OF TAKING BRANCH
FROM MAIN
FIG. 29. METHOD
OF DRIPPING MAIN WHERE
IT RISES TO HIGHER LEVEL
/f. — Suitable for vapor and atmospheric
systems.
FIG. 30. LOOPING
MAIN AROUND
BEAM
OQT POCKET
FIG. 34. DIRT
POCKET
CONNECTION
TRAP
L SUPPLY MA\N
FIG. 31. LOOPING DRY
RETURN MAIN AROUND
OPENING
ATo^.— -Suitable for any dry return line and any
return line' carrying air* .
REDUCING CQUPUNQ-x,
FIG. 35, DRIPPING END OF
MAIN INTO WET RETURN
,2Vote.-— Suitable- for* vapor systems.
554
CHAPTER 32 — PIPING FOR STEAM HEATING SYSTEMS
DBY PETUBU-
•
FIG. 36. DRIPPING END OF MAIN INTO FIG. 37. DRIPPING HEEL OF RISER INTO
DRY RETURN. (A GATE VALVE is DRY RETURN. (A GATE VALVE is
RECOMMENDED AT THE INLET RECOMMENDED AT THE INLET
SIDE OF THE TRAP) SIDE OF THE TRAP)
The pipe sizes would then be based on the length of the run and the pressure drop
desired, as in the case of radiators. It generally is considered desirable to place the in-
direct heating units on a separate system and not on supply or return lines connected to
the general heating system.
DRIPPING
Any steam main in any type of steam heating system may be dropped
to a lower level without dripping if the pitch is downward with the steam
flow. Any steam main in any heating system can be elevated if dripped
(Fig. 29). Steam mains also may be run over obstructions without a
change in level if a small pipe is carried below the obstruction to care for
the condensation (Fig, 30). Return mains may be carried past doorways
or other obstructions by using the scheme illustrated in Fig. 31 ; in vacuum
systems it is well to have a gate valve in the air line.
Offsets in steam and return piping should preferably be made with
90-deg ells but occasionally fittings of other angles are used, and in such
cases the length of the diagonal offset will be found as shown in Fig. 32.
Branches from steam mains in one-pipe gravity steam systems should
use the preferred connection shown in Fig. 33, but where radiator condensa-
tion does not flow back into the main the acceptable method shown in the
same figure may be used. This acceptable method has the advantage^
giving a perfect swing joint when connected to the vertical riser or radia-
tor connection, whereas the preferred connection does not give this swing
without distorting the angle of the pipe. Runouts from the steam main
are usually made about 5 ft long to provide flexibility for movement in
the main.
Dirt pockets, desirable on all systems employing thermostatic traps,
should be so located as to protect the traps from scale and muck which
will interfere with their operation. Dirt pockets are usually made 8 in.
to 12 in. deep and serve as receivers for foreign matter which otherwise
would be carried into the trap. They are constructed as shown in Fig. 34.
On vapor systems where the end of the steam main is dripped down
into the wet return, the air venting at the end of the main is accomplished
by an air vent passing through a thermostatic trap into the dry return
line as shown in Fig. 35. On vacuum systems the ends of the steam mains
are dripped and vented into the return through thermostatic drip traps
opening into the return line. The same method may be used in atmos-
pheric systems. The cooling leg (Fig. 36) is for cooling the condensation
555
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
sufficiently before it reaches the trap so the trap will not be held shut by
too high a temperature. On down-feed systems of atmospheric, vapor,
and vacuum types, the bottom of the steam risers are dripped in the
manner shown in Fig. 37.
PROBLEMS l\ PRACTICE
1 • What is the equivalent length of run in a steam system?
It is the length of straight pipe which will have the same friction and pressure drop as a
shorter length of pipe of the same size with accompanying valves, tees, elbows, and other
fittings will have, when both pipes are carrying the same amount of steam at the same
pressure.
2 • When the size of pipe is still undetermined, what arbitrary percentage is
usually added to the actual length to obtain the equivalent length?
Usually 100 per cent; in other words, the actual length is doubled to allow for the added
drop produced by the valves, tees, elbows, and other fittings.
3 • What are the major factors to be considered in determining the flow of
steam in pipes?
a. The initial steam pressure available and the total pressure drop allowable between the
source of steam supply and the end of the return system. The pressure drop should
never exceed one half of the initial pressure.
b. The maximum steam velocity allowable. When condensate is flowing against the
steam, the velocity must not be so great as to produce water hammer, or hold up
water in parts of the system until the steam flow is reduced sufficiently to permit the
water to pass. The velocity at which disturbances take place depends upon :
1. Size of pipe.
2. Whether pipe is vertical or horizontal.
3. Pitch or grade of pipe.
4. Quantity of water flowing against steam.
c. The equivalent length of run from the source of steam supply to the farthest heating
unit, with allowance for friction in pipe fittings and valves.
4 • Name three fundamental considerations in designing the piping system
for steam heating.
a. Provision for the distribution of suitable quantities of steam to the various heating
units.
b. Provision for the return of condensate from the radiators and piping to the boiler.
c. Provision of means for expelling air from the radiators and piping.
5 • Why is the proper reaming of the ends of pipe necessary?
The capacities of pipes depend upon the free area available for flow. In cutting the pipe
this area may be restricted by a burr, which may decrease the capacity of a pipe more
than 25 per cent in the smaller pipe sizes.
6 • a. What are the major factors to he considered when selecting a pressure
reducing valve?
b. How should such valve be installed?
a. The initial pressure of the steam must be considered along with the desired reduced
pressure. The connected load to be supplied must be known in square feet of equiva-
556
CHAPTER 32 — PIPING FOR STEAM HEATING SYSTEMS
lent direct radiation or in pounds of steam per hour. For operation with a continuous
load, a semi-balanced or double seated valve operated by a diaphragm gives good
results. Where the load is intermittent, as in process work or with thermostatically
controlled blast heaters, a so-called dead end or single seated valve should be used.
The pressure reducing valve should be installed in a horizontal line with a gate valve
on each side, and with a by-pass operated by a valve. The pressure balancing pipe
from the diaphragm chamber should be connected into the top or side of the low
pressure main not less than 15 ft from the reducing valve.
7 • What is the usual expansion allowance and how it is compensated for in
heating system supply risers?
The expansion of low pressure stearn piping is normally taken as 1J^ to 1^ in. per 100
ft of pipe. With a five story building a double swing connection between the riser and the
main will suffice. In buildings between 5 and 10 stories high the riser should be anchored
near its center and have double swing connections to the main. For taller buildings
expansion loops or riser offsets are used which are capable of handling a length of riser
reaching 5 stories in either direction from the joint. The risers are anchored at each
alternate 5 stories. All radiators must have double swing connections, and those con-
nected above where the riser is anchored must be given greater pitch to insure their
having proper grade when the riser is heated.
8 • Why should all boiler steam supply tappings be used full size?
In order to operate at low steam velocities so the water in suspension can separate from
the steam and remain in the boiler.
9 • What is the Underwriters Loop or the Hartford Connection?
An arrangement of piping on the returns to low pressure boilers wherein the return line
is raised up nearly to the water line of the boiler and is then dropped back and con-
nected to the boiler return inlet; the high point is connected by a balance pipe to the
steam runout from the boiler on the boiler side of all stop valves. With this loop no
check valve is required, and water cannot be backed out of the boiler and into the return
at a point lower than the invert of the pipe at the top of the loop.
10 • What are the important factors in making radiator connections?
Connections to radiators should be made as direct as possible, of proper size, with ample
pitch of piping and allowance for expansion.
11 • Why should careful attention be given to proper dripping and drainage
of steam piping?
The steam mains and risers must be quickly drained of condensate and where necessary
vented of air in order to obtain a sufficient supply of steam to the radiators. Proper
drainage is also necessary to insure a noiseless heating system.
12 • What is the limit of pressure drop usually recommended in a vacuum
system?
Not over y% Ib (2 02) per 100 ft of equivalent run, and not over 1 Ib total drop.
13 • When steam and condensation are flowing in the same direction, what is
the maximum total pressure drop which should be used?
The maximum total pressure drop should not exceed one half of the initial steam pressure.
14 • What does a proper installation of a pressure reducing valve include?
A strainer in front of the pressure reducing valve; a gate valve in front of the strainer; a
gate valve after the reducing valve; a by-pass around the two gate valves, strainer f and
pressure reducing valve; and a globe valve in the by-pass. Sometimes a safety valve on
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
the low pressure side and pressure gages on both sides are installed. The high pressure
line should be dripped just before the high pressure steam enters the pressure reducing
valve assembly,
15 • Will a pressure reducing valve which is reducing the steam pressure from
100 Ib gage to 50 Ib gage pass more or less steam than the same valve when
reducing the steam pressure from 100 Ib gage to 5 Ib gage?
The valve will pass practically the same volume of steam in each case as the velocity of
steam flowing through an orifice shows no material increase after the reduced absolute
pressure has fallen to 58 per cent of the initial absolute pressure. Because of its greater
density, the weight of steam passed will be greater in the case of the reduction to 50 Ib
gage.
558
Chapter 33
HOT WATER HEATING SYSTEMS
AND PIPING
One- and Two-Pipe Systems, Selecting Pipe Sizes, Forced Circu-
lation, Effect of Variations in Pipe Sizes, Gravity Circulation,
Mechanical Circulation, Expansion Tanks, Installation Details
A HOT water heating system is one in which water is the medium by
which heat is carried through pipes from the boiler to the heating
units. There are two general types, namely, forced circulation and gravity
circulation systems. In the former the pressure head maintaining flow is
produced mechanically, whereas in the latter the pressure head is pro-
duced by the differences in weight of the water in the flow and in the
return risers.
The fundamental rule in the design of a hot water system is that the
total friction and resistance head in any circuit must equal the pressure
head causing the water to flow in the same circuit.
In designing a hot water heating system, it is necessary to determine :
1. The heat losses of the rooms or spaces to be heated. (See Chapter 7.)
2. The size and type of boiler. (See Chapter 25.)
3. The location, type, and size of heating units. (See Chapter 30.)
4. The method of piping.
5. Suitable pipe sizes.
6. The type and size of circulating pump (if forced circulation).
7. The type and size of expansion tank.
The unit, a square foot of equivalent direct radiation, E,DR, has been used
for many years for rating purposes in both steam and hot water systems, but
its use, especially in hot water systems, has always resulted in complications
and confusion. It is the plan of THE GUIDE to eventually eliminate this
empirical expression and to substitute a logical unit based on the Btu. The
Mb, the equivalent of 1000 Btu, and the Mbh, the equivalent of 1000 Btu
per hour, which have been approved by the A.S.H.V.E., are used in this
chapter on hot water systems to replace the square foot of radiation formerly
used.
ONE- AND TWO-PIPE SYSTEMS
Pipe systems may be divided into two general types, namely, two-pipe
and one-pipe systems. In a two-pipe system the piping is arranged so that
the water flows through only one radiator during a circuit through the
system, so that all radiators are supplied with water at practically the
same temperature as that in the boiler. In a one-pipe system, the water
flows through more than one radiator during its circuit. In that case, the
559
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
first radiator receives the hottest water; the second radiator, somewhat
cooler water; the third one, still cooler; and so on. As the temperature of
the water supplied to a radiator is lowered, the size of the radiator must
be increased and, consequently, the total heating surface for a one-pipe
system must be greater than that for a two-pipe system for the same
service.
Two-pipe systems may be divided into two classes, direct return sys-
tems (Fig. 1), and reversed return systems (Fig. 2). In a direct return
system the water returns to the heater by a direct route after it has
passed through its radiator and, as a result, the paths through the three
radiators shown in Fig. 1 are of unequal lengths, the path through the
first radiator being the shortest and that through the third radiator, the
longest. In a reversed return system, the water returns to the heater by
an indirect route after it has passed through the radiators, so that the
paths leading through the three radiators shown in Fig. 2 are practi-
cally of equal length.
The reversed return system has an advantage over the direct return
system in that it is more likely to function satisfactorily even though the
FIG. 1. A DIRECT RETURN SYSTEM
FIG. 2. A REVERSED RETURN SYSTEM
pipe system is not accurately designed. For example, if in Fig. 2 all pipes
are of one size, each of the three radiators will receive approximately the
same quantity of hot water because the three paths are practically of
-equal length, whereas in Fig. 1, if all pipes are of the same size, Radiator
1 will receive more water than the others because the path through it is
shorter than those through the other radiators. As a result, Radiator 1
will be filled with water at a higher average temperature than the re-
maining two radiators, and will therefore dissipate more heat. To pre-
vent this unequal distribution of heat it is necessary to throttle the paths
through Radiators 1 and 2 so that the friction heads of the three paths are
<equal when each radiator receives its proper quantity of water.
A comparison of Fig. 1 and Fig. 2 may suggest that a reversed return
system requires considerably longer mains than a direct return system.
This is not always the case. For example, note the reversed return
system of Fig. 3.
PIPE SIZES
The pressure heads available in forced circulation systems are much
larger than those in gravity circulation systems, consequently, higher
velocities may be used in designing the system, with the result that smaller
pipes may be selected and the first cost of the installation reduced. As
the pipes of a heating system are reduced in size, the necessary increase in
560
CHAPTER 33 — HOT WATER HEATING SYSTEMS AND PIPING
the velocity of the water increases the cost of operating the circulating
pump. There is an optimum velocity of the water in a heating system for
which the sum of the cost of the system and the cost of its operation is a
minimum. This velocity should be determined by calculation for the-
particular system under consideration.
Since the velocities in forced circulation systems are higher than those
in gravity circulation systems, and since the friction heads in a heating
system vary almost as the squares of the velocities, a given error in the
calculation or assumption of a velocity is less important in a forced circu-
lation system than in a gravity circulation system and, consequently, it
t/z"
I'A."
54
C| 14-2.
L.
G
12
_r_
H
GG
4-
GG
54-
ilk"
At
FIG. 3. A FORCED CIRCULATION REVERSED RETURN SYSTEM*
aThis system could be divided into two branches. This would permit the use of smaller pipes and would
produce only slight changes in the total length of the pipe. It is shown as a single system here simply to-
illustrate the method of determining pipe sizes by means of pipe size tables. Note that the numbers on
the radiators indicate thousands of Btu per hour (Mbh) and not square feet.
is easier to design a satisfactory forced circulation system than a satis-
factory gravity circulation system.
FORCED CIRCULATION
The following examples will illustrate the procedure to be followed in
designing forced circulation systems:
Example 1. Assume that the paths through the five radiators shown in. Fig. 3 consist
each of 150 ft of mains, 5 ft of radiator connections, 1 boiler, 1 radiator, 1 radiator valve,
10 ells, and 2 tees. Design the piping for this system.
Solution. The friction heads in the boiler, radiator, valve, and tee may be expressed
in terms of the friction head in one elbow according to the values given in Table 1.
Having done this, each of the five circuits is taken as 155 ft of pipe and about 24 elbow
equivalents. The friction head of one elbow is approximately equivalent to that in a
pipe having a length equal to 25 diameters. Assuming that the average pipe size in this
case will be about 1 l/i in., one elbow equivalent may be placed equal to about 3 ft of pipe
and the total length of the circuit equivalent to about 227 ft of pipe.
Having determined the equivalent pipe length, assume the rate at which the water i*
561
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
1000
j
'SO .0< 500 \W
HCAT CONVEYELD PE* HOUB IN 1000 5, T. U,
Tfcc DirrcccNCC JN TCMPCPATUEC or THE WATER IN Tnt. FLOW AND SCTURN Itotw
10000
FIG, 4. FRICTION HEADS IN PIPES FOR A 20 F TEMPERATURE DIFFERENCE
OF THE WATER IN THE FLOW AND RETURN LINES
CHAPTER 33 — HOT WATER HEATING SYSTEMS AND PIPING
to be forced through the system. This rate may vary widely. The water may flow
through the radiator so that it will cool 10 deg or 20 deg or any other reasonable number
of degrees. In this case, assume a 10-deg drop. Since the system is to dissipate 66,000
Btu per hour (66 Mbh), the pump must circulate 6600 Ib of water per hour or 13.8 gpm
based on the actual density of water of 7.99 Ib per gallon at 215 F. One gallon of water
per minute at this density will deliver 9600 Btu per hour (9.6 Mbh) with a temperature
drop of 20 F.
TABLE 1. ELBOW EQUIVALENTS'*
1 90-deg elbow._ ., 1.0
1 45-deg elbow 0.7
1 90-deg long turn elbow 0.5
1 open return bend 1.0
1 open gate valve 0.5
1 open globe valve 12.0
1 angle radiator valve 2.0
1 radiator. 3.0
1 heater.-.. 3.0
1 tee (Noteb)
aThe loss of head in one elbow can be expressed in terms of the velocity head by the formula:
1/2
where
h = the loss of head in feet, v =* the velocity of approach in feet per second,
and 2g = 64.4 ft per second per second.
l>The loss of head in tees when water is diverted at right angles through a branch of the tee varies with
the per cent diverted. When the water diverted is less than 60 per cent of that approaching the tee, the
loss of head, in elbow equivalents, may be expressed as follows:
** - 3
where
A« «= the loss of head in elbow equivalents, vi = the velocity of approach,
vt = the velocity of water diverted at right angles.
Values in elbow equivalents for the most common percentages of water diverted in a Ixlxl-in. tee are
as follows:
25% ______ ............................................................................... 16.0
33% ........................................................................................ 9.0
100^r////rr//r////™^ 1.8
For other percentages the approximate values may be secured by interpolation. When the water is
diverted from the tee into a smaller size branch, as in a IxlxK-ia- tee, approximate values may be secured
by means of Formula 2.
The next step in the design is to assume the velocity at which the water is to circulate
through the system. This also may vary materially. As the velocity is increased, the
sizes of the pipes and the cost of the system are decreased, but the cost of operating the
circulating pump is increased. The designing engineer should make a careful study to
determine the velocity which will produce the most economical installation for the
particular case in hand. In this case, assume a velocity of about 1H fps for a lJ<C-m.
pipe.
Reference to Fig. 4 shows that for a IJ^-in. pipe and a velocity of 18 in. per second,
the friction head is about 100 milinches per foot, or about 2 ft for a circuit of 227 ft, if
the pipe sizes for that circuit are chosen so that the average friction head is about
100 milinches per foot of pipe.
The pipe sizes may now be selected from Fig. 4 by making allowance for the fact that
Fig. 4 is based on a temperature drop of 20 F and that the system to be designed is to
have a temperature drop of only 10 F as follows: Sections AB and KA carry 66,000
Btu per hour (66 Mbh) with a temperature drop of 10 F; if the temperature drop were
20 F these sections would, with the same velocity and the same friction head, carry
132,000 Btu per hour (132 Mbh). Hence, refer to Fig. 4 for 132,000 Btu and a unit
friction head of 100 milinches, and note that the correct size would be about halfway
between a l%~in, and a 2-in. pipe. Therefore, select a !J4-in. pipe for Section AB and
563
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
a 2-in. pipe for Section KA . The pipe sizes for the remaining eight sections and for the
radiator connections can be selected in the same manner and recorded on the pipe
diagram as shown.
The circulating pump for the system should be one which has its highest efficiency
when it is delivering 13.8 gpm against a head of 2 ft,
If a number of heating systems are to be designed for similar conditions,
i.e., for a total friction head of 2 ft and a temperature drop through the
radiators of 10 F when the maximum quantity of heat is being delivered
to the building, a table such as Table 2 may be prepared from the data of
Fig. 4. Having this table, the pipe sizes for the system of Example 1 can
be easily selected. For example, for Sections BC and JK, each supplying
54 Mbh, the equivalent pipe length of the system is 227 ft. In the table
the length shown nearest to this length is 200 ft. In the 200-ft column,
a 1^-in. pipe is slightly too small and a 2-in. pipe is too large. The
l3/£-in. pipe will therefore be selected. For Sections CD and IJ, supplying
42 Mbh, a IJ^-in. pipe is too small and a 1^-in. pipe is too large, so 1J^ in-
will be selected for the flow and 1J^ in. for the return line. For larger
TABLE 2. CAPACITIES OF PIPES IN Mbh (1000 Bxu PER HOUR) AND Velocities of
Water in Pipes in Inches per Second FOR FORCED CIRCULATION SYSTEMS
WITH A TOTAL FRICTION HEAD OF 2 FT AND FOR A MAXIMUM
TEMPERATURE DROP OF 10 Fa
I
2
3
4
5
6
7
8
9
PIPE
SIZE
(INCHES)
EQUIVALENT
LENGTH
OP PIPE
(FEBTb)
EQUIVALENT TOTAL LENGTH OF PIPE IN FEET IN LONGEST CIRCUIT
100
150
200
250
300
350
400
UNIT FRICTION HEAD, IN MILINCHES
240
160
120
96
80
69
60
1A
1
8.8
15
4.8
12
4.1
10
8.4
9
2.9
8
2.6
7.5
8.4
7
%
2
18.8
18
10. 8
14
8.6
12
7.3
11
6.8
10
6.0
9
5.5
8,5
i
2.3
86.0
22
19.8
17
16.3
15
14-4
13
12.5
12
12.0
11
11.1
10.5
IK
3.0
52.8
27
40.8
21
84.8
18
SI. 8
16
27.8
15
26.4
14
84-0
13
iH
3.5
79.2
30
60.7
23
51.2
20
45.6
18
40.8
16
40.0
15
86.0
14
2
4.0
158.8
36
120.0
28
104.0
24
93.5
22
86.4
20
81.5
18
78.8
17
2M
6.0
250. 0
41
198.0
32
164.5
28
149.0
25
189.2
22
185.8
21
122.5
19
3
6.5
444-0
48
348.0
37
294.0
32
270.0
29
254.0
26
840.0
24
228.0
22
«For other temperature drops the capacities of pipes are to be changed correspondingly. For example,
for a temperature drop of 30 F, the capacities shown in this table are to be multiplied by 3. The velocities
remain unchanged,
^Approximate length of pipe in feet equivalent to one elbow in friction head. This value varies with the
velocity.
564
CHAPTER 33 — HOT WATER HEATING SYSTEMS AND PIPING
systems, it will be economical to operate with higher friction heads, and
tables may be prepared similar to Tables 3 and 4, which are based on
total friction heads of 6 and 18 ft, respectively.
Example 2, Design a direct return two-pipe forced circulation system for the layout
shown in Fig. 5. For this system the length of the pipe line from the boiler to the
highest radiator on the farthest riser and back to the boiler is about 250 ft. There are
about 16 elbow equivalents having an equivalent pipe length of about 50 ft, so the total
equivalent pipe length is about 300 ft.
Solution. The same pipe size tables may be used as those developed for the reversed
return system of Fig. 3. Since this system is somewhat larger than that shown in Fig. 3,
Table 3 which provides for a friction head of 6 ft may be used instead of Table 2 which
provides for a friction head of only 2 ft.
Referring to the column for an equivalent total length of 300 ft for Sections AB and
KA, each supplying 117.6 Mbh, it will be found that a 1 J^-in. pipe is too small and a 2-in.
pipe is too large. Consequently, a lj^-in. pipe is selected for the flow line AB, and a
2-in. pipe for the return line KA. For Sections BC and JK, each supplying 88 Mbh, a
IJ^-in. pipe is only slightly too small and it is selected. The remaining pipe sizes are
selected in a similar manner and recorded in Fig. 5. For a temperature drop of 10 F,
24.5 gpm of water must be circulated. The pump to select is one which has its highest
efficiency when it is delivering 24.5 gpm against a 6-ft head.
TABLE 3. CAPACITIES OF PIPES IN Mbh (1000 Bxu PER HOUR) AND Velocities of
Water in Pipes in Inches per Second FOR FORCED CIRCULATION SYSTEMS
WITH A TOTAL FRICTION HEAD OF 6 FT AND FOR A MAXIMUM
TEMPERATURE DROP OF 10 Fa
1
2
3
4
5
6
1
8
PIPE
SIZE
(INCHES)
EQUIVALENT
LENGTH
OF PIPE
(FffiETb)
EQUIVALENT TOTAL LENGTH OF PIPE IN FEET IN LONGEST CIRCUIT
200
300
400
600
800
1000
UNIT FRICTION HEAD, IN MILINCHES
360
240
180
120
90
72
1A
1
7.4
18
6.0
15
5.0
13
8.8
10
a S.4
9
3.1
7.5
U
2
15.8
22
12.7
18
10.8
16
8.4
12
7.7
11
6.7
9
i
2.5
30.0
27
24.0
22
20.4
19
15.8
15
13.9
13
18.5
11
IK
3.3
64-8
33
6Q.5
26
44*4
23
33.6
18
30.0
16
26.8
14
i«
4.0
96.0
37
76.8
31
64.8
26
50.1
20
44. 7
18
40. 8
15
2
5.0
19%. 0
44
15S.O
36
1SO.O
30
100.1
24
90.0
21
78.0
18
VA
6.0
$00.0
50
844-0
41
206.0
35
161.0
26
144.0
24
130.0
21
3
7.5
550.0
58
436. 0
48
S68.0
42
287.0
32
249.0
27
228,0
24
aFor other temperature drops the capacities of pipes are to be changed correspondingly. For example,
for a temperature drop of 30 F, the capacities shown in this table are to be multiplied by 3. The velocities
remain unchanged.
^Approximate length of pipe in feet equivalent to one elbow in friction head. This value varies with
the velocity.
565
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
To secure a correct distribution of hot water among the several risers it is necessary,
as previously stated, to introduce special resistances to balance the several risers, as
follows:
The first riser is 80 ft nearer the boiler than the fifth riser. In order that the two may
be balanced, i.e., that they may operate under equal pressure heads, resistance must be
added to the first riser equal to the friction head in the 80 ft of flow main from B to F
plus that in the 80 ft of return main from G to K.
It will be noted from Table 3 that the unit friction head is about 240 milinches per
foot. The total friction head in the flow and return mains between the first and fifth
risers is therefore 160 X 240 or 38,400 milinches, or a little more than 3 ft, which must be
supplied by additional resistance in the first riser to prevent its having an advantage
over the fifth riser.
This resistance can be supplied by a calibrated and adjusted modulating valve or by
an orifice resistor in a union. If the orifice resistor is to be used, its size may be selected
from Table 5 as follows:
The lower part of the first flow riser supplies 28.8 Mbh. According to Table 3, it
should be a 1-in. pipe and would have a velocity of 22 in. per second, if it were supplying
24 Mbh. Since it is supplying 28.8 Mbh, the velocity will be about 26 in. per second.
From Table 5 it will be found that for a 1-in. pipe and a velocity of 24 in. per second, an
0.45-in. orifice will produce a loss of head of 37,000 milinches. For a velocity of 26 in.
per second, the loss of head will be somewhat more, probably about 43,000 milinches; the
TABLE 4. CAPACITIES OF PIPES IN Mbh (1000 BTU PER HOUR) AND Velocities of
Water in Pipes in Inches per Second FOR FORCED CIRCULATION SYSTEMS
WITH A TOTAL FRICTION HEAD OF 18 FT AND FOR A MAXIMUM
TEMPERATURE DROP OF 10 Fa
1
2
3
4
s
6
7
PIPE
SIZE
(INCHES)
EQTTIVALHNT
LENGTH
OF PIPE
(Firob)
EQUIVALENT TOTAL LENGTH OP PIPE IN FEET IN LONGEST CIRCUIT
200
400
600
800
1000
UNIT FRICTION HuAii, IN MILINCHES
1080
540
360
270
216
1A
1.0
IS. 7
32
8.6
23
7.8
18
6.2
15
5.6
13
H
2.0
87.5
40
18.7
28
15.1
22
18.7
19
11.5
17
1
2.5
55.0
4$
86.8
34
so.o
27
86.4
23
88.6
20
IK
3.0
188. 0
59
81.5
42
66.0
33
58.S
28
50.5
25
1H
4.0
188.0
66
188.0
46
98.8
37
86.8
31
74.8
27
2
5.0
371,0
80
£58.0
56
201.0
45
180.0
38
151.0
33
2^
7.0
598.0
91
407.0
65
S2S.O
51
887.0
43
840.0
3$
3
9.0
1110. 0
107
790.0
76
598.0
60
587.0
51
443.0
44
*For other temperature drops the capacities of pipes are to be changed correspondingly. For example,
for a temperature drop of 30 F, the capacities shown in this table are to be multiplied by 3. The velocities
remain unchanged.
^Approximate length of pipe in feet equivalent to one elbow in friction head. This value varies with
the velocity.
566
CHAPTER 33 — HOT WATER HEATING SYSTEMS AND PIPING
difference between it and the required resistance will be about 10 per cent, which is per-
missible, and the 0.45-in. orifice is selected.
The sizes of the orifice resistors for the second, third, and fourth risers are selected in
a similar manner and found to be 0.45 in,, 0.50 in., and 0.55 in., respectively.
If the design of the system of Fig. 5 is to be extremely refined, the
gravity pressure heads produced by the risers should be taken into con-
sideration. With water at 220 F and 210 F, respectively, in the risers, the
gravity head is 50 milinches per foot of water column or 25 milinches per
foot of flow and return pipe. The pump pressure head in this case is 240
milinches per foot of pipe, and the gravity head, being only one tenth as
large as the pump head, may be neglected without serious error. This is
generally done.
Temperatures of 220 F and 210 F would be used only during the coldest
FIG, 5. A FORCED CIRCULATION DIRECT RETURN SYSTEM
weather for which the system is designed. At other times the tempera-
tures would be lower, the temperature drop smaller, and the gravity heads
smaller. The pump pressure head remains constant throughout the
season if the pump is operated at a constant speed and, consequently, the
gravity head is generally less than one-tenth of the pump head.
Effect of Variations in Pipe Sizes
The pipe sizes for the several parts of the system selected from the
tables are only approximately correct but the resulting error should be
negligible as may be seen from the following study. Assume, as an
extreme case, that the error in pipe size is so large that the water flows
twice as fast through one of the radiators as through the others. This
would make the friction head through this radiator almost four times as
large as those through the other radiators. The result would be that the
water, in flowing through the radiator, would cool 5 F instead of 10 F.
The mean water temperature in the radiator would then be 217)^ F in-
stead of 215 F, and the mean temperature difference, water to air, would
be 147J^ F instead of 145 F. The heat dissipated by the radiator would
therefore be about 2 per cent more than calculated. It is evident that
this difference in heat dissipation is smaller than the difference between
567
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 5.
FRICTION HEADS (IN MILINCHES) OF CENTRAL CIRCULAR
DIAPHRAGM ORIFICES IN UNIONS
DIAMETER
OP
ORIFICES
(INCHES)
VELOCITY OF WATER IN PIPE IN INCHES PER SECOND
24
36
%-in. Pipe
0.25
1300
2900
5000
11,300
20,800
32,000
45,000
0.30
650
1450
2500
5700
10,400
16,000
23,000
57,000
0.35
330
740
1300
2900
5200
8000
12,000
26,000
47,000
0.40
170
380
660
1500
2600
4000
6800
13,000
24,000
53,000
0.45
185
330
740
1300
2000
2900
6500
12,000
27,000
0.50
155
350
620
970
1400
3200
5700
13,000
0.55
75
170
300
480
700
1600
2800
6400
1-in. Pipe
0.35
900
2000
3500
7800
14,000
22,000
32,000
0.40
460
1000
1800
4000
7200
12,000
17,000
37,000
65,000
0.45
270
570
1000
2300
4100
6400
9300
21,000
37,000
0.50
160
330
580
1400
2300
3700
5400
12,000
22,000
50,000
0.55
190
330
750
1300
2200
3000
7000
13,000
28,000
0.60
200
440
800
1300
1800
4200
7400
17,000
0.65
120
260
460
720
1100
2400
4300
10,000
. Pipe
0.45
1000
2250
4000
8900
16,000
25,000
36,000
0.50
660
1450
2600
5800
10,400
16,400
23,000
53,000
0.55
430
950
1700
3800
6800
10,500
15,000
34,000
60,000
0.60
280
630
1100
2500
4400
6900
10,000
22,000
40,000
0.65
190
420
750
1700
3000
4700
6700
15,000
27,000
60,000
0.70
285
510
1150
2000
3100
4500
10,000
18,000
40,000
0.75
190
330
750
1300
2100
3000
6700
12,000
26,000
ly^-in. Pipe
0.55
850
1900
3300
7400
13,000
21,000
30,000
0.60
600
1300
2300
5400
8600
16,800
21,000
50,000
0.65
400
850
1500
3600
7200
10,400
14,000
30,000
53,000
0.70
260
600
1100
2600
4400
7000
10,000
21,000
39,000
0.75
180
400
760
1800
3000
5000
7000
14,000
28,000
0.80
300
540
1200
2200
3200
5000
10,200
19,000
45,000
0.85
200
380
860
1600
2300
3000
7800
13,000
30,000
$-in. Pipe
0.70
890
1850
3500
7400
14,000
22,300
33,000
0.80
470
975
1800
3900
7400
11,700
17,000
37,000
0.90
255
560
1000
2200
4200
6500
9500
20,500
38,000
1,00
160
340
610
1320
2520
4000
5800
12,500
23,000
49,000
1.10
214
375
850
1600
2500
3700
7900
14,000
30,000
1.20
195
460
950
1360
1910
4200
8100
16,800
1.30
275
525
980
1375
3100
4400
8850
practically true in the tests to determine the losses of head in orifices in $£-inM 1-in., and l&-in. pips, con-
ducted by the Texas Engineering Experiment Station, and also in the tests to determine the losses of head
in orifices in 4-in., 6-in., and 12-in. pipe, conducted by the Engineering Experiment Station of the University
of Illinois, (Bulletin 109, Table 6, p. 38, Davis and Jordan).
568
CHAPTER 33 — HOT WATER HEATING SYSTEMS AND PIPING
the calculated heat losses and the actual heat losses, and also smaller than
the average difference between the calculated radiator sizes and the
nearest stock sizes selected.
GRAVITY CIRCULATION
For gravity circulation, the one-pipe system shown in Fig. 6 and the
two-pipe direct return system shown in Fig. 7 are probably in most
common use.
The one-pipe system has the disadvantage that the radiator nearest the
FIG. 6. A ONE-PIPE GRAVITY CIRCULATION SYSTEM
, ^
[mtbh!
V» V
14 Mbd 1
FIG. 7. A TWO-PIPE DIRECT RETURN GRAVITY CIRCULATION SYSTEM
boiler is the only one which receives water at approximately the tem-
perature at which it leaves the boiler. All other radiators receive cooler
water and must be proportionally increased in size, so the total heating
surface in the system Is considerably larger than that in a corresponding
two-pipe system.
The pipe sizes in gravity circulation systems may be varied. As the
pipe sizes are decreased, the temperature drop through the radiators,
which produces circulation, is increased and it becomes necessary to
increase the temperature of the water leaving the boiler so that the mean
temperature in the radiator remains constant. For example, Fig. 8 shows
569
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
diagrammatically an elementary heating system which will function with
either l}^~in. or 1-in. pipe. The radiator is required to deliver 27 Mbhr
and the circuit consists of 30 ft of pipe and 20 elbow equivalents.
If IJ^-in. pipe is used, the system will operate correctly if the water
temperatures in the flow and return risers are 200 F and 180 F, respectively.
The mean water temperature in the radiators will then be 190 F and,
if the radiator is located in air having a temperature of 70 F, the size of
the radiator must be sufficient to deliver 27 Mbh under these conditions.
If 1-in. pipe is used, the system will function correctly with water tem-
peratures in the flow and return risers of 210 F and 170 F, or of 200 F
and 160 F. In the first case, the mean water temperature is again 190 F
and the same size radiator may be used as with the IJ^-in. pipe, but the
temperature of the water leaving the boiler must be raised from 200 F to
210 F. In the second case, the temperature of the water leaving the
boiler is the same as for the 1^-in. pipe, but the mean water temperature
FIG. 8. AN ELEMENTARY SYSTEM
in the radiator is lowered from 190 F to 180 F, and theoretically the size
of the radiator should be increased about 12J^ per cent to deliver the
required 27 Mbh (See Table 3, Chapter 6, 1933 GUIDE).
This indicates the extent to which pipe sizes and radiator sizes may be
decreased by increasing the temperatures of the water in the boiler, as is
possible in closed systems and in open systems in which the open
expansion tank is located sufficiently high to secure a pressure in the
boiler equal to that existing in the boiler of the closed system.
Example S. Design a one-pipe gravity circulation system for the layout shown in
Fig. 6. Assume that the main circuit consists of 150 ft of pipe, 7 elbows, and one boiler.
Solution. Replace the boiler by 3 elbow equivalents and assume that the size of the
main will be about 2 in. According to Table 6, Column 2, a 2-in. elbow is equivalent to
4 ft of pipe, and the total equivalent length of the main will be about 150 plus 40, or
190 ft. Assuming that the center of the boiler will be about 4 ft lower than the horizontal
portion of the main and that the temperature drop in the system is to be 35 F, Table 6
may be used to determine the size of the mains. Note from Column 8, for a 200-ft
length, that a 2-in. main will supply 48 Mbh and a 2j^-in. main, 75,4 Mbh. Since the
system to be designed is to supply 66 Mbh, a 2-in. pipe is too small and a 2H-in. pipe
too large. The solution is to use some 2-in. and some 2J4-in. pipe- Since the 2H-m. is
nearer the correct size than the 2-in., select 2-in. pipe for the first 50 or 60 ft out of the
boiler and 2J^-in. for the remaining pipe back to the boiler.
Tables 7 and 8 may be used to design the radiator risers and connections. According
to Table 7, for 12 Mbh the flow riser should be % in. and the return riser 1 in., and the
riser branches should be 1 in. and 1 Ji in,, respectively. Note that according to Table 8,
both radiator tappings should be 1 in. To simplify the construction, select 1-in. flow
risers with 1-in. riser branches and 1-in. radiator tappings. Also select IMrin. return
risers with lM-in. riser branches, and 1 J^-in. radiator tappings. Similarly, for 18 Mbh,
select 1-5^-in. flow and return risers and riser branches, and lj^-in. radiator tappings.
570
CHAPTER 33 — HOT WATER HEATING SYSTEMS AND PIPING
TABLE 6. CAPACITIES OF MAINS IN Mbh, FOR ONE-PIPE AND FOR TWO-PIPE DIRECT
RETURN GRAVITY CIRCULATION SYSTEMS WITH A TOTAL FRICTION HEAD
OF 0.6 IN., A TEMPERATURE DROP OF 35 F, WHEN THE MAINS
ARE 4 FT ABOVE THE CENTER OF THE BOILER
1
2
3
4
5
6
7
8
9
10
n
PIPE
SIZE
(INCHES)
EQUIVALENT
LENGTH
OF PIPE
(FEETa1)
EQUIVALENT TOTAL LENGTH OP PIPE IN FEET IN LONGEST CIRCUIT
75
100
125
ISO
175
200
250
300 1 350
UNIT FRICTION HEAD, IN MILINCHES
8.0
6.0
4.8
4.0
3.4
3.0
2.4
2.0
1.7
llA
3.0
43.0
57.5
33.0
80.0
27.0
85.0
22.2
20.2
18.7
2
4.0
83.0
72.0
63.0
57.0
51.0
48.0
42.0
38.0
35.0
m
4.5
140.0
115.0
100.0
90.0
81.5
754
67.2
61.0
56.0
3
5.0
234,0
204.0
176.5
160.0
143.0
133.0
110.0
107.5
100.0
3H
5.5
847.0
SOO.O
260.0
236.0
214.0
200.0
177.0
160.0
146.0
4
6.0
490.0
422.0
870.0
334.0
297.0
278.0
248.0
223.0
205.0
aApproxirnate length of pipe in feet equivalent to one elbow in friction head. This value varies with
the velocity.
To develop a rule for determining radiator sizes, assume a system
similar to that of Fig. 6, in which the total temperature drop is to be 35 F
and which is equipped with 7 radiators, all radiators dissipating equal
quantities of heat. The mean temperature of the water in the radiators
will be reduced 5 F for each successive radiator. If the mean tempera-
ture of the water in the first radiator is 200 F, the mean temperature of the
TABLE 7. MAXIMUM CAPACITIES OF RisERsa IN Mbh, AND Velocities of Water in
Pipes in Inches Per Second FOR ONE-PIPE AND FOR TWO-PIPE DIRECT
RETURN GRAVITY CIRCULATION SYSTEMS WITH A DROP OF
35 F THROUGH EACH RADIATOR
PIPE SIZE (INCHES)
IST FLOOR&
2ND FLOOR
3RD A.NB 4TH FLOORS
or PIPE (FHKTC)
Vel. (In.perSec.)<i
Flow
Return
Flow
Return
l/L
1A
• 1.0
5
6.2
1^
%
M
8.0
%
%
1.5
9
2.3
2.3
W.I
14.0
%
1
12
3.2
2.0
12.8
17.1
I
1
2.0
18
2.5
2.5
20
26.0
I
l/*i
21
3.0
2.0
25.2
34
1J^
3.0
26
3.0
3.0
43
55
1J^
1J^
S4
4.0
2.5
i«
m
3.5
43
3.0
3.0
«*This table is based on pressure heads of 450, 1800, 3150, and 4500, respectively, for the first, second,
third, and fourth floor radiators, and on friction heads of 200 milinches for the first floor radiators and con-
nections, and 700 milinches for all other radiators and their connections.
bThe riser branches, the piping which connects the risers to the mains, are to be one size larger than the
oApproximate length of pipes in feet equivalent to one elbow in friction head. This value varies with
the velocity.
^Velocities apply to the riser branches.
571
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
-water in the seventh radiator will be 170 F, and, according to Table 3,
Chapter 6, of the 1933 GUIDE, the heat dissipation of these two radiators
will be to each other as 868 is to 617, or as 140 is to 100, and therefore if
the last radiator is to dissipate as much heat as the first, its size must be
40 per cent larger.
Example 4- Design a two-pipe, direct return, gravity circulation system for the lay-
out shown in Fig. 7. Assume that the main circuit from the boiler to the farthest flow
riser and from the farthest return riser back to the boiler consists of 160 ft of pipe,
6 elbows, and 1 boiler.
Solution. Replacing the boiler by 3 elbow equivalents and assuming that the largest
size of the main will be about 3 in., the total equivalent length of the main will be 160
plus 45, or 205 ft. Assuming that the center of the boiler will be about 4 ft lower than the
horizontal portion of the main, and that the temperature drop will be 35 F for the
system, the pressure head caused by the difference in weight between the water in the
TABLE 8. MAXIMUM CAPACITIES OF RADIATOR CONNECTIONS IN Mbh, FOR ONE-PIPE
AND FOR Two- PIPE DIRECT RETURN GRAVITY CIRCULATION SYSTEMS WITH
A TEMPERATURE DROP OF 35 F THROUGH EACH RADIATOR
PIPE SIZE
IST FLOOR
2ND, 3RD, AND 4TH FLOORS
EQUIVALENT LENGTH
Flow
Return
Off PIPE (FEET&)
Mbh
Mbk
yz
y*
1.0
4.1
5.9
3^
%
5.2
7.5
3A
%
1.5
7.0
10.5
H
i
9.1
13.0
l
i
2.0
12.5
17.8
l
1M
17,5
23.2
IK
1M
3.0
23. 3
33.2
aApproximate length of pipe in feet equivalent to one elbow in friction head. This value varies with
•the velocity.
flow and return risers joining the mains to the boiler will be about 0.6 in. of water, or
about one-fortieth of the pressure head produced by the circulating pump selected for the
system of Fig. 3.
Table 6 may be used to determine the size of the main as follows: Refer to Column 8
and note that for Sections AB and IA, which supply 105.6 Mbh, a 3-in. pipe is too large
and a 2M-in. pipe is too small; hence, select 2J^ in. for Section AB and 3 in. for Section
IA. For Sections BC and HI, which supply 76.8 Mbh, a 2}^-in. pipe is almost exactly
the correct size and is selected for both sections.
For the forced circulation system of Fig. 5, the pressure head produced by the circu-
lating pump is used to force the water through the mains and also through the risers.
Gravity circulation systems have two distinct pressure heads. One is produced by the
difference in weight of the water in the flow and return risers adjacent to the boiler, and
is the boiler pressure head, which in this case is 0.6 in. The other pressure head is pro-
duced by the difference in weight of the water in the flow and return risers adjacent to
the radiators, and is the radiator pressure head. If the temperature drop through the
radiators is about 35 F, and if the story heights of the building are 9 ft and the distance
from the center of the first floor radiator to the average level of the main is 3 ft, the
radiator pressure head of the first floor radiator is about 450 milinches and the pressure
heads of the radiators on the upper floor are 1350 milinches greater than those on the
next lower floors.
Tables 6 and 7 are based on the assumption that the boiler pressure head must be
•equal to the friction head in the mains, and that the several radiator pressure heads must
be equal to the respective radiator and riser friction heads,
To design the radiator risers, use Table 7 and begin with the set nearest the boiler.
The first floor risers must supply 28.8 Mbh. According to the table, lM-in. flow and
return risers will supply 26.0 Mbh; if the return riser is increased to 1 J^ in., the capacity
will be increased to 34,0 Mbh, This is considerably larger than necessary, and lM~in.
flow and return risers are selected. However, it must be remembered that the riser
572
CHAPTER 33 — HOT WATER HEATING SYSTEMS AND PIPING
branches, which are the connections from the flow and return mains to the flow and
return risers, are to be one size larger than the risers.
The second floor risers must supply 19.2 Mbh. According to the table, the capacity
of 1-in. flow and return risers is 20.0 Mbh, and that size is selected.
The third floor risers must supply 9.6 Mbh. If a 3^-in. flow and a %-in. return riser
are used, the capacity will be 8.0 Mbh; if both risers are % in., the capacity will be
14.0 Mbh. The %-in- pipe is selected for both risers.
To design the radiator connections, use Table 8 and note that for the first floor
radiator connections the capacity of a M-in. flow and 1-in. return is 9.1 Mbh, and that of
a 1-in. flow and a 1-in. return is 12.5 Mbh. The former is more nearly the correct size,
but since it is difficult to secure a good flow through first floor radiators, the 1-in. flow
and return connection is selected. For the two upper floors, the capacity of a %-in. flow
and return connection is 10.5 Mbh, and that size is used.
As explained in the design of the forced circulation system of Fig. 5,,
the two-pipe direct return system of Fig. 7 will not function correctly
unless its four sets of risers are balanced among themselves. This neces-
sary balancing is accomplished by adding resistances to all risers, except
the one farthest from the boiler, equal to the excess boiler pressure heads-
available for those risers above the boiler pressure head available for the
farthest riser. For example, the first set of risers is 60 ft nearer the boiler
than the last set. Since the flow and return mains are designed for a
friction head of 3 rnilinches per foot (See Table 6, Column 8), the boiler
pressure head available for the first set of risers is 360 rnilinches in excess
of that available for the fourth set. The velocity in the riser branch is
3 in. per second (See Table 7) and, therefore, according to Table 5, an
0.65-in. orifice in a 1^-in. union should be used. This will provide a
resistance of about 420 rnilinches. In the same manner it is found that
for the second set of risers a resistance of 240 rnilinches is required and
that an 0.70-in. orifice in a 1%-in. union will provide a resistance of 285
rnilinches. For the third set of risers, a resistance of 120 rnilinches is
required and an 0.60-in. orifice in a 1-in. union will provide sufficient
resistance.
MECHANICAL CIRCULATION
Circulating pumps for hot water systems may be used to provide the
motive head for forced circulation systems as already described, or to
improve the operation of gravity-designed systems. Small specially-
designed centrifugal pumps installed on a by-pass with the necessary gate
or check valves near the point where the return main enters the heater
maybe employed. Specially-designed, electrically-driven, propeller-type
circulating pumps or units may also be employed. The latter are usu-
ally installed directly in the return main and are available for all com-
mercial pipe sizes used for hot water heating. The motor switch may be
under manual control, automatic control using thermostatic elements,
or tied in with the oil or gas burner switch which starts and stops the
burner. For large capacities these units may be installed in multiple.
For exceptionally large installations such as central heating plants, cir-
culating pumps of the centrifugal single stage type, having an average
operating efficiency of 70 per cent against heads up to 125 ft, are some-
times used. It is generally advisable to install the pumps in duplicate to
provide for contingencies and to insure continuous operation. In such
cases each pump may be made equal to two-thirds of the maximum
capacity required.
573
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
EXPANSION TANKS
When water at ordinary temperatures is heated or cooled, its volume is
increased or decreased. This variation in the volume of the water in a
heating system Is generally provided for by means of an expansion tank
into which the water can flow from the system during the heating-up
periods and from which it can flow back into the system during the
cooling-down periods.
The expansion tank may be open or closed. In an open expansion tank
(Fig. 9), the water is subjected to atmospheric pressure and can expand
freely without a material increase in pressure. In a closed expansion
tank (Fig. 10), the water is subjected to the pressure of the compressed air
VENT-** ,
OVERFLOW $, VENT
OVERFLOW
GAUGE
GLASS
CIRCULATION
P'lPE
EXPANSION
TANK
Q — PRESSURE
j GAUGE
^- Gu.oae VALVE
EXPANSION
TANK
GATE VALVEV
CW.SUPPLY'
{DATE VALVE To DRAIW
-GATE VALVE
PIPE
FIG, 9. AN OPEN EXPANSION TANK
-DRAIN
FIG. 10. A CLOSED EXPANSION TANK
within the tank, and as the water expands, the volume of the air in the
tank is decreased and its pressure increased.
The open expansion tank must be placed at a sufficient elevation above
the highest radiator to prevent boiling when the water in that radiator is
at the highest temperature to which it is to be heated. For example, if
the water is to be heated to 225 F on extremely cold days, the absolute
pressure on the water in the highest radiator must be at least 19 Ib per
square inch. This pressure will be secured if the open expansion tank is
located 15 ft above the highest radiator. If a closed expansion tank is
used and is located 30 ft below the highest radiator, an absolute pressure
of about 32 Ib per square inch must be maintained in the expansion tank
if the water in the highest radiator is to be heated to 225 F without danger
of boiling.
The type of expansion tank used in a heating system, whether open or
closed, has no influence on the operation of the system. The only function
performed by the expansion tank is to provide for the variation in the
volume of the water in the system, and at the same time to maintain a
sufficient pressure in the system to prevent boiling when the water is at
the highest temperature for which the system is designed. The use of an
expansion tank may be dispensed with when the heating system is
allowed to float on the water system, i.e., when the connection between
574
CHAPTER 33 — HOT WATER HEATING SYSTEMS AND PIPING
the heating system and the water system is kept open so that the water
system replaces the expansion tank.
The capacity of the expansion tank should be at least twice the in-
crease in volume produced when the water in the system is heated from
its normal to its maximum temperature. When 25 gal of water are heated
from 40 F to 200 F, the volume of water increases to 26 gal. A safe rule,
therefore, is to make the water capacity of the expansion tank equal to
10 per cent of the capacity of the heating system.
In a forced circulation system, the expansion tank should be connected
to the return main near the circulating pump. In a gravity circulation
system, the expansion tank should be connected to the flow riser so that
air liberated from the water in the boiler may escape through the ex-
pansion tank, except where it is desired to maintain a temperature higher
than 212 F, in which case the connection should be in the return main to
prevent possible boiling in the expansion tank.
The expansion tank should be protected so that the water in the tank
or in the connecting pipe lines cannot freeze. If such water should freeze
and the water in the system be heated to cause further expansion, the
resulting force will burst the boiler or some other portion of the system.
INSTALLATION DETAILS
The detailed installation of the pipe system should be governed by
four fundamental rules:
1. All piping must be pitched either up or down so that all gases which are liberated
from the water can move freely to a vented section of the system. Whenever practicable,
the pipe line should be pitched so that gases flowing to a vent will flow in the same direc-
tion as the water. When a pipe system cannot be installed without creating air pockets,
that is, sections in the system from which liberated gases cannot escape, such sections
must be provided with automatic air relief valves or with air valves which may be
operated manually when necessary.
2. All piping must be arranged so that the entire system can be drained, either to
permit alterations or repairs, or to prevent freezing if the system is not to be operated
during a cold period.
It is well to install a gate valve and union in every riser near the main to permit the
draining of individual risers without draining the entire system. It is also well, in large
installations, to divide the system into branches and to provide each branch with unions
and valves so that any one branch can be drained without disturbing the remaining
ones.
The dividing of large heating systems into branches or zones and providing each zone
with individual valves has the further advantage of permitting a varying temperature
control. For example, if a building is equipped with a forced circulating system and if
the south rooms are on one branch of the main and the north rooms are on a separate
branch, the valves may be set so that the water will circulate through the north branch
with a temperature drop of, say, 10 F, and through the south branch with a tempera-
ture drop of, say, 20 F, thus delivering less heat to the south rooms than to the north
rooms. This arrangement is especially valuable when the regulating valves are controlled
thermostatically by the temperatures in the two zones, because no matter how accurately
the heating system may have been designed, the heat demand of any group of rooms
varies with sunshine and with wind velocity, and these intermittent variations can be
provided for only by the individual control made possible by changing the valve settings
controlling the heat supplied to particular groups of rooms.
3. All piping must be installed so that it is free to expand and contract with changes of
temperature without producing undue stresses in the pipes or connections. For this
purpose it is generally sufficient to allow for a variation in length of 1 in. for 100 ft of pipe.
575
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
4. The pipe system must be installed so that each circuit has its correct friction head.
To bring this about, it is necessary in some cases to minimize the friction, i.e., to make
the pipe line as short as possible and to provide as few fittings as possible; and in other
cases it is necessary to increase the length of the pipe and the number of fittings so that,
for every circuit, the friction head will be equal to the available pressure head.
The connections from the boiler to the mains should be short and direct, to reduce the
friction head. It is frequently possible to avoid an elbow and to reduce the length of the
pipe by running the pipe in a diagonal direction, either in a horizontal or in a vertical
plane.
The mains and branches should pitch up and away from the heater, generally not
less than 1 in. in 10 ft. The flow main should always be covered; the return main should
be covered except where it is to provide the heating surface for the basement.
The connections from mains to branches and to risers should be such that circulation
through the risers will start in the right direction. Hence, in a one-pipe system the flow
connection must be nearer the heater than the return connection. In a correctly-
designed two-pipe system, the pressure in the flow main is higher than that in the return
FIG. 11. METHOD OF CONNECTING RADIATOR
TO ALLOW FOR EXPANSION OF PIPE
main, and a slight variation in the distances of the flow and return connections from the
heater is not material; but it is generally best to have the two connections about equally
distant from the heater.
In some cases it may be advisable to take the flow connection off the top of the main
and the return connection from the side, but in most cases both connections should be at
an angle of 45 deg. This method shortens the lines and substitutes 45-deg ells for
90-deg ells.
Preferably, connection of the flow riser to a radiator should be to the upper tapping,
and connection of the return riser to a radiator should be to the lower tapping. When
hot water enters at the top of a radiator it will distribute itself along the entire length of
the radiator, and as it cools it will settle gradually to the bottom; the cool water may
then be taken out of the radiator at either end.
With forced circulation and high velocities, it is advisable to let the water enter at the
top of the radiator and leave at the bottom of the opposite end. With gravity circulation
and low velocities it makes little difference whether the water leaves at the end at which
it enters or at the opposite end.
The connections of the risers to the radiators should be such that provision is made for
the vertical expansion of the risers. This can be accomplished as indicated in Fig, 11 by
using one tee and two ells for each connection. These connections should be pitched
upward or downward, whichever may be necessary to prevent the formation of air
pockets and to permit draining.
576
CHAPTER 33 — HOT WATER HEATING SYSTEMS AND PIPING
PROBLEMS IN PRACTICE
1 • What causes the circulation of water in hot water heating systems?
In gravity systems, circulation is caused by the difference between the weight of the cool
water in the return riser and that of the hot water in the flow riser.
In forced circulation systems, circulation is produced primarily by a pump, and second-
arily by the difference in the weights of the water in the return and flow risers. However,
the secondary effect is so small when compared with that of the circulating pump that
it may be neglected in most cases.
2 • What tends to prevent or to retard the circulation of water in hot water
heating systems?
In both gravity flow and forced circulation systems, the friction which must be overcome
when the water is flowing through pipes, fittings, valves, heaters, and radiators tends to
prevent or retard circulation. For a given pipe the friction varies approximately as the
1.7 power of the velocity, and for given fittings, valves, heaters, and radiators, the friction
varies approximately as the square of the velocity. It is therefore sufficiently accurate
to express the friction in fittings, valves, heaters, and radiators in terms of the friction
in one standard elbow, as shown in Table 1.
3 • In the elementary heating system, Fig. 8, what is the pressure head main-
taining the circulation if the water in the return riser is at 180 F and that in
the flow riser is at 200 F?
It is found, from Table 8, Chapter 1, that 180 F water weighs 60.61 Ib per cu ft and 200 F
water weighs 60.13 Ib per cu ft. The pressure head is independent of the size of the
pipe. If the two risers were each 1 ft square, the water in the flow riser would weigh
601.3 Ib and that in the return riser would weigh 606.1 Ib. Thus the water in the return
riser would weigh 4,8 Ib more than that in the flow riser. Consequently, the resulting
pressure head is 4.8 Ib per square foot.
Pressure heads are generally expressed in feet, or inches, or milinches of water of a given
temperature. In this case we are dealing with water at both 180 F and 200 F, so the
pressure head is expressed in terms of 190 F water. Such water weighs 60.39 Ib per cu ft,
and to secure a pressure of 4.8 Ib per square foot, it is necessary to have a column of
water having a weight of 4.8 divided by 60.39 = 0.0795 ft, or 0.9540 in., or 954 milinches.
This is the pressure head which maintains the circulation.
4 • In the elementary system of Question 3, if the radiator dissipates 14,000
Btu per hour, what is the velocity of the water in the pipe line, if the pipes are
1 in. in diameter? What, if they are % in. in diameter?
Since the temperature drop through the radiator is from 200 F to 180 F or 20 F, every
pound of water flowing through the radiators delivers 20 Btu; consequently, 14,000
divided by 20 = 700 Ib of water, or for 190 F water, 700 divided by 60.39 » 11.59 cu ft
of water must flow through the radiator and through the pipe lines every hour.
The interior area of a 1-in. pipe is 0.864 sq in. The velocity in the 1-in. pipe is 11.59
divided by 0.864 and multiplied by 144 = 1932 ft per hour or 6.44 in. per second.
For %-in. pipe, the interior area is 0.533, and the velocity is 6.44 multiplied by 0.864
and divided by 533 — 10.44 in. per second.
5 • If, in the elementary heating system of Question 3, a 1-in. pipe line is
used, what would be the friction head?
If the radiator is connected as shown in Fig. 11, with the heater connected to provide
freedom of expansion, the heating circuit may be assumed to consist of a heater, 25 ft of
pipe, 8 elbows, 1 radiator valve, and 1 radiator. From Table 1 it appears that the heater
and radiator are equivalent, in friction, to 6 elbows; hence, the circuit may be placed
equal to 25 ft of pipe and 14 elbows.
From the diagram of Fig. 4 it appears that the friction head for a 1-in. pipe and a velocity
577
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
of 6.44 in. per second is about 25 milinches per foot. For 25 ft of pipe, the friction head
will be 625 milinches.
vz
It appears from Table 1 that the friction head in one elbow is — , or in this case 0.54
•^g
multiplied by 0.54 and divided by 64.4 « 0.0045 ft or 54 milinches. Hence, for the 14
elbows the friction is 756 milinches. For the entire circuit, the friction head is the sum
of the 625 milinches of the pipe plus the 756 milinches of the elbows, or 1381 milinches
which equal 1.381 in.
6 • If the elementary heating system of Question 3 is installed with a 1-in.
pipe line, how will it function?
It is found from the answer to Question 3 that the pressure head is 954 milinches and
from the answer to Question 5 that the friction head is 1381 milinches when the water is
flowing with such velocity that the specified 14,000 Btu will be delivered with a 20 F
temperature drop through the radiators. Since the pressure head is smaller than the
friction head, the system will not function as planned for the water will flow through the
system more slowly and remain in the radiator longer. The temperature drop through
the radiator will be more than 20 F, and the difference in the weight of the water in the
return and flow risers will be greater than that intended. The final result will be that the
pressure head will become equal to the friction head at a value somewhere between
954 and 1381 milinches. Since the average water temperature in the radiator will be
less than 190 F, the radiator should be larger than the size given in Question 4.
7 • Should a hot water heating system be designed to embody small pipes or
large pipes?
As pipe sizes in gravity circulation heating are reduced, the friction head is increased-
and it is necessary to increase the temperature drop through radiators; this lowers the
average temperature of the water in the radiators and necessitates an increase in the
size of the radiators, so whereas the cost of the pipe in a system is reduced, the cost of the
radiators is increased. For each installation there is a definite pipe size which entails
maximum economy.
As pipe sizes in forced circulation systems are reduced, friction heads are increased so a
circulating pump of greater size or capacity is required. Thus, by decreasing the size of
the piping, both the first cost of the circulating pump and the cost of its operation are
increased. There is a definite pipe size for every installation which is most economical.
For each installation of both types of systems there is a definite pipe size entailing maxi-
mum economy which can be determined by a series of comparative calculations.
8 • What should be the size of the radiators for the elementary heating system
of Question 3 in which the water enters the radiator with a temperature of
200 F and leaves with a temperature of 180 F? The average temperature of the
water in the radiator is, approximately, 190 F.
If test results are available for the particular radiators to be used, and for the tempera-
tures named, the size of the radiators should be selected from them. If no such test
results are to be had, but if test results are available for the type of radiator to be used
when it is supplied with 215 F steam and placed in a 70 F room, the required size may be
determined by the following ratio: The required size is to the corresponding steam
radiator size as (215 — 70)1-3 is to (190 - 70)1-3. This ratio works out to 1.28. Hence,
the radiators should be 28 per cent larger under the conditions prescribed than are cor-
responding radiators under standard conditions. It is immaterial whether a radiator is
filled with steam or with water, as long as the average temperature of its outer surface
is the same in both cases.
578
Chapter 34
PIPE, FITTINGS, WELDING
Pipe Material, Types of Pipe Used, Dimensions of Pipe Com-
mercially Available, Expansion and Flexibility of Pipe, Pipe
Threads and Hangers, Types of Fittings, Welding as Applied to
Erection of Piping, Valves, Corrosion of Piping
IMPORTANT considerations in the selection and installation of pipe
and fittings for heating, ventilating, and air conditioning work are
dealt with in this chapter.
MATERIALS
Use of corrosion-resistant materials for pipe, including special alloy
steels and irons, wrought-iron, copper and brass, has increased con-
siderably during the past few years. The recent development of copper,
brass, and bronze fittings which can be assembled by soldering or sweating
permits the use of thin-wall pipe and thereby has reduced the initial cost
of such installation. The following brief discussion indicates the variety
of pipe materials and the types of pipe available.
Wrought-Steel Pipe. Because of its low price, the great bulk of wrought
pipe used for heating and ventilating work at the present time is of
wrought steel. The material used for steel pipe is a mild steel made by
the acid-bessemer, the open-hearth, or the electric-furnace process.
Ordinary wrought-steel pipe is made either by shaping sheets of metal
into cylindrical form and welding the edges together, or by forming or
drawing from a solid billet. The former is known as welded pipe, the
latter as seamless pipe.
Many types of welded pipe are available, although the smaller sizes
most frequently used in heating and ventilating work are made by the
lap-weld or butt-weld process. While the lap-weld process produces a
better weld than the butt type, lap-weld pipe is seldom manufactured in
nominal pipe sizes less than 2 in. Seamless pipe can be obtained in the
small sizes at a somewhat higher cost.
Seamless steel pipe is frequently used for high pressure work or where
pipe is desired for close coiling, cold bending, or other forming operation.
Its advantages are its somewhat greater strength which permits use of a
thinner wall and, in the small sizes, its freedom from the occasional
tendency of welded pipe to split at the weld when bent.
Wrought-iron Pipe. Wrought-iron pipe is considered to be more corro-
sion-resisting than ordinary steel pipe and therefore its somewhat higher
first cost can be justified on the basis of longer life expectancy. Wrought-
iron pipe may be identified by the spiral line marked into each length,
either knurled into the metal or painted on it in red or other bright color.
579
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Otherwise, there is little difference in the appearance of wrought-iron and
steel pipe, although microscopic examination of polished and etched
specimens will readily disclose the difference.
Cast Ferrous Pipe. There are now available several types of cast
ferrous-metal pipe made of a good grade of cast-iron with or without
additions of nickel, chromium, or other alloy. This pipe is available in
sizes from 1 J^ in. to 6 in., and in standard lengths of 5 or 6 ft with external
and internal diameters closely approximating those of extra-strong
wrought pipe. Cast ferrous pipe may be obtained coupled, bevelled for
welding, or with ends plain or grooved for the several types of couplings.
It is easily cut and threaded as well as welded. The fact that it is readily
welded enables the manufacturers to supply the pipe in any lengths
practicable for handling.
Alloy Metal Pipe. Steel pipe bearing a small alloy of copper or other
alloying element, such as molybdenum or manganese, has been claimed
to possess more resistance to corrosion than plain steel pipe and it is
advertised and sold under various' trade names.
Copper Pipe and Fittings. Owing to its inherent resistance to cor-
rosion, copper and brass pipe have always been used in heating, venti-
lating, and water supply installations, but the cost with standard dimen-
sions for threaded connections has been high. The recent introduction
of fittings which permit erection by soldering or sweating allows the use
of pipe with thinner walls than are possible with threaded connections,
thereby reducing the cost of installations.
The initial cost of brass and copper pipe installations generally runs
higher than the corresponding job with steel pipe and screwed connections
in spite of the use of thin-wall pipe, but the corrosive nature of the fluid
conveyed or the inaccessibility of some of the piping may warrant use of
a more expensive material than plain steel. The advantages of corrosion-
resisting pipe and fittings should be weighed against the correspondingly
higher initial cost.
DIMENSIONS
The /PS dimensions of commercial pipe universally used at the present
time conform to the recommendations made by a Committee of the
A.S.M.E. in 1886. Pipe up to 12 in, in diameter is made in certain
definite sizes designated by nominal internal diameter which is somewhat
different from the actual internal diameter, depending on the wall thick-
ness required. There are three weights of wrought-iron and steel pipe
commonly used, known as standard-weight, extra-strong, and double-extra-
strong. Because of the necessity of maintaining the same external dia-
meter in all three weights for the same nominal size, the added wall
thickness is obtained by decreasing the internal diameter. The term
full-weight, when applied to sizes below 8 in,, means that the pipe is up to
the nominal weight per foot. When applied to sizes between 8 and 12 in.,
inclusive, it often indicates that the pipe has the heaviest of several wall
thicknesses listed. In sizes 14 in. and upward, pipe is designated by its
outside diameter (O.D.) and the wall thickness is specified.
While the demands for pipe for the heating and ventilating industry are
reasonably well served by the standard-weight and extra-strong pipe,
580
CHAPTER 34 — PIPE, FITTINGS, WELDING
demands for pipe for higher pressures and temperatures in industry
resulted in the use of a multiplicity of wall thicknesses for all sizes. Even
in heating installations, the erection of piping by welding was deemed to
warrant the use of pipe lighter than standard weight. For these reasons,
a Sectional Committee on Standardization of Wrought Iron and Wrought
Steel Pipe and Tubing functioning under the procedure of the American
Standards Association was appointed to standardize the dimensions and
materials of pipe.
The proposed pipe standard recommended by that sectional committee
has set up several schedules of pipe including standard-weight and extra-
strong thicknesses which are now included in Schedules 40 and 60, re-
spectively. The schedules approved by the Sectional Committee are
given in Tables 1 and 3 and the corresponding weights in Tables 2 and 4.
Standard-weight pipe is generally furnished with threaded ends in
random lengths of 16 to 22 ft, although when ordered with plain ends,
5 per cent may be in lengths of 12 to 16 ft. Five per cent of the total
number of lengths ordered may be jointers which are two pieces coupled
together. Extra-strong pipe is generally furnished with plain ends in
random lengths of 12 to 22 ft, although 5 per cent may be in lengths of
6 to 12 ft.
EXPANSION AND FLEXIBILITY
The increase in temperature of a pipe from room temperature to an
operating steam or water temperature one hundred degrees or more above
room temperature results in an increase in length of the pipe for which
provision must be made. The amount of linear expansion (or contraction
in the case of refrigeration lines) per unit length of material per degree
change in temperature is termed the coefficient of linear expansion of
that material, or commonly, the coefficient of expansion. This coefficient
varies with the material.
The linear expansion of cast iron, steel, wrought-iron, and copper pipe,
the materials most frequently used in heating and ventilating work, can
be determined from Table 5.
The elongation values in Table 5 were computed from the following
formula :
1000 ") + H"1000" ' I (1)
•where
Lt = length at temperature t degrees Fahrenheit, feet.
Z0 » length at 32 F, feet.
t = final temperature, degrees Fahrenheit.
a and b are constants as follows:
METAL
a
6
Cast- Iron
0.005441
0.001747
Steel . , .,.
0.006212
0.001623
Wrought- Iron . ...
0.006503
0.001622
CoDoer „
0.009278
0.001244
581
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
The three methods by which the elongation due to thermal expansion
may be taken care of are:
1. Expansion joints.
2. Swivel joints.
3. Inherent flexibility of the pipe itself utilized through pipe bends, right-angle turns,
or offsets in the line.
Expansion joints of the slip-sleeve, diaphragm, or corrugated types
made of copper, rubber, or other gasket material are all used for taking
TABLE 1. DIMENSIONS OF WELDED AND SEAMLESS STEEL PIPE
NOMINAL
PIPE SIZE
OUTSIDE
DJAM.
NOMINAL WA.LL THICKNESSES FOR SCHEDULE NUMBERS
Schedule
10
Schedule
20
Schedule
30
Schedule
4:0
Schedule
60
Schedule
80
Schedule
100
Schedule
120
Schedule
140
Schedule
160
y*
H
H
ilA
Vi
2
m
3
m
4
5
6
8
10
12
14 O. D.
160.D.
18 O. D.
20 0. D.
24 0. D.
30 O. D.
0.405
0.540
0.675
0.840
1.050
1.315
1.660
1,900
2.375
2.875
3.500
4.000
4.500
5.563
6.625
8.625
10.75
12.75
14.0
16.0
18.0
20.0
24.0
30.0
0.068*
0.095*
0.088*
0.119*
0.091*
0.126*
0.109*
0.147*
0.187
0.218
0.250
0,250
0.281
0.343
0.375
0.437
0.113*
0.154*
0.133*
0.179*
0.140*
0.191*
0.145*
0.200*
0.154*
0.218*
0.203*
0.276*
0.216*
0.300*
0.226*
0.318*
0.237*
0.337*
0.437
0.531
0.625
0.718
0.906
1.125
1.312
1.406
1.562
1.750
1.937
2.312
0.258*
0.375*
0.500
0.280*
0.432*
0.562
O."25(f
0.250
0.250
0.250
0.250
0.312
0.250
0.250
0.250
0.312
0,312
0.312
0.375
0.375
0.500
0.277*
0.307*
0.330*
0.375
0.375
0.437
0.500
0.562
0.625
0.322*
0.365*
0.406
0.437
0.500
0.562
0.593
0.687
0.406
0.500*
0.562
0.593
0.656
0.718
0.812
0.937
0.500*
0.593
0.687
0.750
0.843
0.937
1.031
1.218
0.593
0.718
0.843
0.937
1.031
1.156
1.250
1.500
0.718
0.843
1.000
1.062
1.218
1.343
1.500
1.750
0.812
1.000
1.125
1.250
1.437
1.562
1.750
2.062
All dimensions are given in inches,
The decimal thicknesses Hated for the respective pipe sizes represent their nominal or average wall dimensions and include
an allowance for mill tolerance of 12.5 per cent under nominal thicknesses.
Thicknesses marked with asterisk in Schedules 30 and 40 are identical with thicknesses for standard-weight pipe in
former lists; those in Schedules 60 and 80 are identical with thicknesses for extra-strong pipe in former lists.
The Schedule Numbers indicate approximate values of the expression 1000 x P/S.
up expansion, but generally only for low pressures or where the inherent
flexibility of the pipe cannot readily be used as in underground steam or
hot water distribution lines.
Swivel joints are used extensively in low-pressure steam and hot water
heating systems and in hot water supply lines. The swivel joints absorb
the expansive movement of the pipe by the turning of threaded joints.
In many cases the straight pipe in the offset of a swivel joint is sufficiently
flexible to take up the expansion without developing enough thrust to
produce swiveling in the threaded joint. This is preferable since con-
tinued turning in the threaded joint may in time result in a leak, par-
582
CHAPTER 34 — PIPE, FITTINGS, WELDING
ticularly when the pressure is high. The amount of elongation which a
swivel joint can take up is controlled by the length of the swing piece
employed and by the lateral displacement which is permissible in the
long pipe runs.
Probably the most economical method of providing for expansion of
piping in a long run is to take advantage of the directional changes which
must necessarily occur in the piping and proportion the offsets so that
sufficient flexibility is secured. Ninety-degree bends with long, straight
tangents in either a horizontal or a vertical plane are an excellent means
TABLE 2. NOMINAL WEIGHTS OF WELDED AND SEAMLESS STEEL PIPE
NOMINAL
PIPE
SlZB
INCHES
SCHED.
10
PLAIN
ENDS
SCHED.
20
PLAIN
ENDS
SCHEDULE
30
SCHEDULE
40
SCHED.
60
PLAIN
ENDS
SCHED.
80
PLAIN
ENDS
SCHED.
100
PLAIN
ENDS
SCHED.
120
PLAIN
ENDS
SCHED.
140
PLAIN
ENDS
SCHED.
160
PLAIN
ENDS
Plain
Ends
Threads
and
Coup-
lings
Plain
Ends
Threads
and
Coup-
lings
y*
¥
H
l
M
VA
i
m
3
m
4
5
6
8
10
12
14 0. D.
160.D.
18 0. D.
20 0. D.
240. D.
30 0. D.
0.25*
0.43*
0.57*
0.86*
1.14*
1.68*
2.28*
2.72*
3.66*
5.80*
7.58*
9.11*
10.8*
14.7*
19.0*
28.6*
40.5*
53.6
63.3
0.25*
0.43*
0.57*
0.86*
1.14*
1.69*
2.29*
2.74*
3.68*
5.82*
7.62*
9.21*
10.9*
14.9*
19.2*
28.8*
41.2*
55.0
0.32*
0.54*
0.74*
r~LTL_
1.09*
1.31
1.94
2.85
3.77
4.86
7.45
10.0
14.3
1.48*
2.18*
3.00*
3.64*
5.03*
7.67*
10.3*
12.5*
15.0*
19.0
22.6
33.0
45.3
74.7
116.0
161.0
190.0
241.0
304.0
374.0
536.0
20.8*
27.1
28.6*
36.4
22.4
28.1
33.4
45.7
52.3
59.0
78.6
94.7
158.0
24.7*
34.3*
43.8*
54.6
62.6
82.0
105.0
141.0
197.0
25.0*
35.0*
45.0*
35.7
54.8*
73.2
85.0
108.0
133.0
167.0
231.0
43.4*
64.4
88.6
107.0
137.0
171.0
209.0
297.0
50.9
77.0
108.0
131.0
165.0
208.0
251.0
361.0
60.7
89.2
126.0
147.0
193.0
239.0
297.0
416.0
67.8
105.0
140.0
171.0
224.0
275.0
342.0
484.0
lisT
42.1
47.4
52.8
63.5
99.0
82.8
105.0
123.0
171.0
Weights are given in pounds per linear foot and are for pipe with plain ends except for sizes which are commercially available with
threads and couplings for which both weights are listed.
"The weights marked with asterisk in Schedules 30 and 40 are identical with weights for standard~weight pipe in former lists: those in
Schedules 60 and 80 are identical with weights for extras-strong pipe in former lists.
The Schedule Numbers indicate approximate values of the expression 1000 x P/S.
for securing adequate flexibility with larger sizes of pipe. When flexi-
bility cannot be obtained in this manner, it is necessary to make use of
some type of expansion bend. The exact calculation of the size of ex-
pansion bends required to take up a given amount of thermal expansion
is relatively complicated1, The following approximate method, however,
has been found to give reasonably good results and is deemed to be
sufficiently accurate for most heating work.
Fig. 3, Chapter 32, shows several types of expansion bends commonly
ipiping Handbook, by Walker and Croker, and A Manual for the Design of Piping for Flexibility by
the Use of Graphs, by E, A. Wert, S. Smith, and E. T. Cope, published by The Detroit Edison Company,
583
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
used for taking up thermal expansion. The amount of pipe, L, required
in each of these bends may be computed from the following formula:
(2)
L = 6.16 JDA
where
L = length of pipe, feet.
D = outside diameter of the pipe used, inches.
A- =f the amount of expansion to be taken up, inches.
This formula, based on the use of mild-steel pipe with wall thicknesses
not heavier than extra-strong, assumes a maximum safe value of fiber
stress of 16,000 Ib per square inch. When square type bends are used, the
width of the bend should not exceed about two times the height. It is
*- TABLE 3. DIMENSIONS OF WELDED WROUGHT-IRON PIPE
NOMINAL
PIPE
SIZE
OUTSIDE
DIAMETER
NOMINAL WALL THICKNESSES FOR SCHEDULE NUMBERS
Schedule
10
Schedule
20
Schedule
30
Schedule
40
Schedule
60
Schedule
80
1A
1A
y*
IA
H
m
VA
2
m
3
" 3H
4
5
6
8
10
12
140. D.
16 0. D.
18 0. D.
20 0. D.
0.405
0.540
0.675
0.840
1.050
1.315
1.660
1.900
2.375
2.875
3.5
4.0
4.5
5.563
6.625
8.625
10.75
12.75
14.0
16.0
18.0
20.0
0.070*
0.090*
0.093*
0.111*
0.115*
0.136*
0.143*
0.148*
0.158*
0.208*
0.221*
0.231*
0.242*
0.263*
0.286*
0.329*
0.372*
0.414
0.437
0.500
0.562
0.562
0.098*
0.122*
0.129*
0.151*
0.157*
0.183*
0.195*
0.204*
0.223*
0.282*
0.306*
0.325*
0.344*
0.383*
0.441*
0.510*
0.606
0.702
0.750
0.283*
0.313*
0.336*
0,375
0.375
0,437
0.500
0.510*
0.574
0.625
0.6S7
0.750
0.250
0,250
0.250
0.312
0.312
0.312
0.375
All dimensions are given in inches.
The decimal thicknesses listed for the respective pipe sizes represent their nominal or average wall dimensions and include
an allowance for mill tolerance of 12.5 per cent under the nominal thickness.
•"Thicknesses marked with an asterisk in Schedules 30 and 40 are identical with thicknesses for standariL-weight pipe in
former lists; those in Schedules 60 and 80 are identical with thicknesses for extra-strong pipe in former lists.
The Schedule Numbers indicate approximate values of the expression 1000 x P/S.
further assumed that the corners are made with screwed or flanged elbows
or with arcs of circles having radii five to six times the pipe diameter.
All risers must be anchored and safeguarded so that the difference in
length when hot from the length when cold shall not disarrange the
normal and orderly provisions for drainage of the branches,
It is especially necessary with light-weight radiators so to anchor the
piping and so to give it freedom for expansion that no strain therefrom
shall be allowed to distort the radiators. When expansion strains from
the pipes are permitted to reach these light metal heaters they usually
emit sounds of distress which are exceedingly troublesome.
584
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
supports fitted with rollers, machined blocks, elliptical or circular rings of
larger diameter than the pipe giving contact only at the bottom or trolley
hangers. In all cases, allowance should be made for rod clearance to
permit swinging without setting up severe bending action in the rods.
For pipes of small size, perforated metal strip is often used. For
horizontal mains, the rod or strip usually is attached to the joists or steel
TABLE 5. THERMAL EXPANSION OF PIPE IN INCHES PER 100 Fxa
(For superheated steam and other fluids refer to temperature column)
SATURATED STEAM
ELONGATION IN INCHES PER
100 FT PROM — 20 F UP
SATURATED
STEAM
ELONGATION IN INCHES PER 100
FT FROM —20 F UP
Vacuum
Inches
ofHg.
Pressure
Pounds
per
Square
Inch
Gage
Tem-
perature
Degrees
Fahren-
heit
Cast-
iron
Pipe
Steel
Pipe
Wrought
Iron
Pipe
Copper
Pipe
Pressure
Pounds
per
Square
Inch
Gage
Tem-
perature
Degrees
Fahren-
heit
Cast-
iron
Pipe
Steel
Pipe
Wrought
Iron
Pipe
Copper
Pipe
-20
0
0
0
0
664.3
500
3.847
4.296
4.477
6.110
0
0.127
0.145
0.152
0.204
795.3
520
4.020
4.487
4.677
6.352
20
0.255
0.293
0.306
0.442
945.3
540
4.190
4.670
4.866
6.614
40
0.390
0.430
0.465
0.655
1115.3
560
4.365
4.860
5.057
6.850
29.39
60
0.518
0.593
0.620
0.888
1308.3
580
4.541
5.051
5.268
7.123
28.89
80
0.649
0.725
0.780
1.100
1525.3
600
4.725
5.247
5.455
7.388
27.99
100
0.787
0.898
0.939
1.338
1768.3
620
4.896
5.437
5.660
7.636
26.48
120
0.926
1.055
1,110
1.570
2041.3
640
5.082
5.627
5.850
7.893
24.04
140
1.051
1.209
1.265
1.794
2346.3
660
5.260
5.831
6.067
8.153
20.27
160
1.200
1.368
1.427
2.008
2705
680
5.442
6.020
6.260
8.400
14.63
180
1.345
1.528
1.597
2.255
3080
700
5.629
6.229
6.481
8.676
6.45
200
1.495
1.691
1.778
2.500
720
5.808
6.425
6.673
8.912
"Ts"
220
1.634
1.852
1.936
2.720
740
6.006
6.635
6.899
9.203
10.3
240
1.780
2.020
2.110
2.960
760
6.200
6.833
7.100
9.460
20.7
260
1.931
2.183
2.279
3.189
780
6,389
7.046
7.314
9.736
34.5
280
2.085
2.350
2.465
3.422
800
6.587
7.250
7.508
9.992
52.3
300
2.233
2.519
2.630
3.665
820
6.779
7.464
7.757
10.272
74.9
320
2.395
2.690
2.800
3.900
840
6.970
7.662
7.952
10.512
103.3
340
2.543
2.862
2.988
4.145
860
7.176
7.888
8.195
10.814
138.3
360
2.700
3.029
3.175
4.380
880
7.375
8.098
8.400
11.175
180.9
380
2.859
3.211
3.350
4.628
900
7.579
8.313
8.639
11.360
232.4
400
3.008
3.375
3.521
4.870
920
7.795
8.545
8.867
11.625
293.7
420
3.182
3.566
3.720
5.118
940
7.989
8.755
9.089
11.911
366.1
440
3.345
3.740
3.900
5.358
960
8.200
8.975
9.300
12.180
451.3
460
3.511
3.929
4.096
5.612
980
8.406
9.196
9,547
12.473
550.3
480
3.683
4.100
4.280
5.855
1000
8.617
9.421
9.776
12.747
aFrom Piping Handbook, by Walker and Crocker. This table gives the expansion from —20 F to the
temperature in question. To obtain the amount of expansion between any two temperatures take the
difference between the figures in the table for those temperatures, For example, if a steel pipe is installed
at a temperature of 60 F and is to operate at 300 F, the expansion would be 2.519 - 0.593 «• 1.926 in.
work of the floor above. For long runs of vertical pipe subject to con-
siderable thermal expansion, either the hangers should be designed to
prevent excessive load on the bottom support when expansion takes
place, or the bottom support should be designed to withstand the entire
load.
FITTINGS
Fittings for joining the separate lengths of pipe together are made in a
variety of forms, and are either screwed or flanged, the former being
586
•CHAPTER 34 — PIPE, FITTINGS, WELDING
generally used for the smaller sizes of pipe up to and including 3J^ in.,
and the latter for the larger sizes, 4 in. and above. Screwed fittings of
large size as well as flanged fittings of small size are also made and are
used for certain classes of work at the proper pressure.
The material used for fittings is generally cast-iron, but in addition to
this malleable iron, steel and steel alloys are also used, as well as various
TABLE 6. TENTATIVE AMERICAN STANDARD DIMENSIONS OF ELBOWS, 45 DEC ELBOWS,
TEES, AND CROSSES (STRAIGHT SIZES) FOR 125 LB CAST-IRON SCREWED FITTINGS
ELBOW
TEE
CROSS
A
c
B
E
F
G
H
CENTER
INSIDE DIAMETER
NOMINAL
PIPE
SIZE
TO END,
ELBOWS,
TEES AND
CROSSES
CENTER
TO END,
45 DEG
ELBOWS
LENGTH
OP THREAD
MIN.
WIDTH
OF BAND,
MIN.
OF FITTING
METAL
THICKNESS.
MIN.
OUTSEDB
DIA.MBTBH
OF BAND,
MIN.
Min.
Max.
X
0.81
0.73
0.32
0.38
0.540
0.584
0.110
0.93
0.95
0.80
0.36
0.44
0.675
0.719
0.120
1.12
%
1.12
0.88
0.43
0.50
0.840
0.897
0.130
1.34
%
1.31
0.98
0.50
0.56
1.050
1.107
0.155
1.63
1
1.50
1.12
0.58
0.62
1.315
1.385
0.170
1.95
1M
1.75
1.29
0.67
0.69
1.660
1.730
0.185
2.39
1H
1.94
1.43
0.70
0.75
1.900
1.970
0.200
2.68
2
2.25
1.68
0.75
0.84
2.375
2.445
0.220
3.28
2H
2.70
1.95
0.92
0.94
2.875
2.975
0.240
3.86
3
3.08
2.17
0.98
1.00
3.500
3.600
0.260
4.62
3H
3.42
2.39
1.03
1.06
4.000
4.100
0.280
5.20
4
3.79
2.61
1.08
1.12
4.500
4.600
0.310
5.79
5
4.50
3.05
1.18
1.18
5.563
5.663
0.380
7.05
6
5.13
3.46
1.28
1.28
6.625
6-725
0.430
8.28
8
6.56
4.28
1.47
1.47
8.625
8.725
0.550
10.63
10
8.08
5.16
1.68
1.68
10.750
10.850
0.690
13.12
12
9.50
5.97
1.88
1.88
12.750
12.850
0.800
15.47
14 O.D.
10.40
....
2.00
2.00
14.000
14.100
0.880
16.94
16 O.D.
11,82
....
2.20
2.20
16.000
16.100
1.000
19.30
All dimensions given in inches.
grades of brass or bronze. The material to be used depends on the
character of the service and the pressure.
As in the case of pipe, there are several weights of fittings manufactured.
Recognized American Standards for the various weights are as follow:
Cast-iron pipe flanges and flanged fittings for 25 Ib (sizes 4 in. and larger), 125 Ib, and
250 Ib maximum saturated steam pressure.
587
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Malleable iron screwed fittings for 150 Ib maximum saturated steam pressure.
Cast-iron screwed fittings for 125 and 250 Ib maximum saturated steam pressure.
Steel flanged fittings for 150 and 300 Ib maximum steam service pressure.
The allowable cold water working pressures for these standards vary from 43 Ib for
the 25 Ib standard to 500 Ib for the 300 Ib steel standard.
Screwed fittings include : nipples or short pieces of pipe of varying
lengths; couplings, usually of wrought iron only ; elbows for turning angles
of either 45 deg or 90 deg; return bends, which may be of either the close
or open pattern, and may be cast with either a back or side outlet; tees;
crosses; laterals or Y branches; and a variety of plugs, bushings, caps,
TABLE 7. AMERICAN STANDARD DIMENSIONS OF TEES AND CROSSES (STRAIGHT SIZES)
FOR 125 LB CAST-IRON FLANGED FITTINGS
n
K-A-*t U-A-»t*-A-*l
^fen fefe!
A
IJL
TEE
SIDE OUTLET
CROSS
NOMINAL
PIPE SlZEa-b
A
AA
DIAMETER
OF
FLANGE
THICKNESS OF
FLANGE,
MIN.
METAL
THICKNESS
OF BODY,
MIN.
CENTER TO FACE
TEES AND
CROSSES *>•«
FACE TO FACE
TEES AND
CROSSES b-c
1
IK
3%
7
|g
ge
He
4
8 2
5 8
%. 6
$
2 2
4H
9
6
/"S
2J-£
5
10
7
l^Hlg
7/a
3
5Ji
11
7J^
%
P*
3-^5
6
12
81/g
ljj/£g
4
6Jx£
13
9
Ijjj^g
%
5
7J/£
15
10
*JK6
l^
6
8
16
11
1
9it
8
9
18
13J^
1M
10
11
22
16
Ij^g
%
12
12
24
19
IJi
1^f«
14 O.D.
14
28
21
1 %
H
16 O.D.
15
30
23 J^
1/^L6
1
18 O.D.
16J^
33
25
l?f 6
JK«
20 O.D.
18
36
27 J^
11J^6
24 O.D.
22
44
32
l!%
1J^
30 O.D.
25
50
38%
2H
IJie
36 O.D,
28
56
46
2J^
15^
42 O.D.
31
62
53
25^
l1Me
48 O.D.
34
68
59H
2M
2
All dimensions given in inches.
aSize of all fittings listed indicates nominal inside diameter of port.
bTees, side outlet tees, and crosses, 16 in, and smaller, reducing on the outlet, have the same dimensions
center to face, and face to face as straight size fittings corresponding to the size of the larger opening.
Sizes 18 in, and larger, reducing on the outlet, are made in. two lengths, depending on the size of the outlet.
cTees and crosses, reducing on run only, carry same dimensions center to face and face to face as a
straight size fitting of the larger opening.
588
CHAPTER 34 — PIPE, FITTINGS, WELDING
lock-nuts, flanges and reducing fittings. Reducing fittings a? well as
bushings, both of which are used in changing from one pipe size to another,
may have the smaller connection tapped eccentrically to permit free drain-
age of the water of condensation in steam lines or free escape of air in
water lines.
Threads used for fittings are the same American Standard taper pipe
threads as those used for pipe, and unless otherwise ordered, right-hand
threads are used. To facilitate drainage, some elbows have the thread
TABLE 8. AMERICAN STANDARD DIMENSIONS OF ELBOWS FOR
125 LB CAST-IRON FLANGED FITTINGS
VU/
1 * • 1
SO OEG. LOHGfcADlUS 45OEG, REDUCING SIDE OUTLET
NOMINAL
PIPE SIZE a
CENTER TO FACE
ELBOW b-«-<j
CENTER TO FACE
LONG RADIOS
ELBOW b-o-d
CENTER TO FACE
45 DBG
ELBOW «
DIAMETER
OF
FLANGE
THICKNESS
OP FLANGE,
Mm.
METAL
THICKNESS
OF BODY,
MlN.
1
2 2
3 2
4
5
6
8
10
12
14 O.D.
16 O.D.
18 O.D.
20 O.D.
24 O.D.
30 O.D.
36 O.D.
42 O.D.
48 0,D.
3%
4
7J
8
9
11
12
14
15
18
22
25
28
31
34
5
i*
9
lOJi
11 Ji
14
19
24
26^
29
34
41H
49
64
I*
5
5H
8 2
11
15
18
21
24
9
10
11
16
19
21
23^
25
32
46
53
All dimensions given in Inches.
aSize of all fittings listed indicates nominal inside diameter of port,
^Reducing elbows and side outlet elbows carry same dimensions center to face as straight size elbows
corresponding to the size of the larger opening.
oSpecial degree elbows, ranging from 1 to 45 deg, inclusive, have the same center to face dimensions
as given for 45 deg elbows and those over 45 deg and up to 90 deg, inclusive, shall have the same center to
face dimensions as given for 90 deg elbows. The angle designation of an elbow is its deflection from straight
line flow and is the angle between the flange faces>
outlet elbows shall have all openings on intersection center-lines.
580
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
tapped at an angle to provide a pitch of the connecting pipe of J^ in. to
the foot. These elbows are known to the trade as pitched elbows and are
commercially available. Malleable iron fittings, like brass fittings, are
cast with a round instead of a flat band or bead, or with no bead at all.
Fittings are designated as male or female, depending on whether the
threads are on the outside or inside, respectively.
Flanged fittings are generally used in the best practice for connecting
all piping above 4 in. in diameter. While screwed fittings may be used
for the larger sizes and are satisfactory under the proper working con-
ditions, it will be found difficult either to make or to break the joints in
these large sizes.
A number of different flange facings in common use are plain face,
raised face, tongue and groove, and male and female. Cast-iron fittings
for 125 Ib pressure and below are normally furnished with a plain face,
while the 250 Ib cast-iron fittings are supplied with a J^-inch raised face.
The standard facing for steel flanged fittings for 150 and 300 Ib is a
}^-inch raised face although these fittings are obtainable with a variety of
facings. The gasket surface of the raised face may be finished smooth
or may be machined with concentric or spiral grooves often referred to as
serrated face or phonograph finish, respectively.
The dimensions of elbows, tees and crosses for 125 Ib cast-iron screwed
fittings are given in Table 6, whereas the dimensions for 125 Ib cast-iron
flanged fittings are given in Tables 7 and 8.
For low temperature service not to exceed about 220 F, a number of
paper or vegetable fiber gasket materials will prove satisfactory ; for plain
raised face flanges, rubber or rubber inserted, gaskets are commonly
employed. Asbestos composition gaskets are probably the most widely
used, particularly where the temperature exceeds 250 F. Jacketed
asbestos and metallic gaskets may be used for any pressure and tem-
perature conditions, but preferably only with a relatively narrow recessed
facing.
WELDING
Erection of piping in heating and ventilating installations by means of
fusion welding has been commonly accepted in the past few years as a
competitive method to the screwed and flanged joint. Since the question
of economy of welding as against the use of screwed and flanged fittings
is dependent on the individual job, the use of welding is generally recom-
mended on the basis of a greatly reduced cost of maintenance and repair,
of less weight resulting from the use of a lighter-weight pipe, and of
increased economy in pipe insulation, hangers, and supports rather than
on the basis of any economy that might be effected in actual erection by
welding.
Fusion welding, commonly used in erection of piping, is defined as the
process of joining metal parts in the molten, or molten and vapor states,
without the application of mechanical pressure or blows. Fusion welding
embraces gas welding and electric arc welding, both of which are com-
monly used to produce acceptable welds.
Welding application requires the same basic knowledge of design as do
the other types of assembly, but in addition, requires a generous know-
590
CHAPTER 34 — PIPE, FITTINGS, WELDING
ledge of the sciences involved, particularly as to welding qualities of
metal, their reaction to extremely high temperatures, and the ability to
determine and use only the best quality welding rods. This requirement
applies equally to employer and employee with the employer accepting
all of the responsibility. Thus the employer should select his welding
mechanics with good judgment, provide them with first-class equipment
and tools, arrange for their training and use of acceptable workmanship
standards, and at regular intervals subject their work to prescribed tests.
a. TYPICAL SHORT RADIUS ELBOWS
b. TEE c. FORGED CAP
FIG. 1. TYPICAL WELDING FITTINGS
d. CONCENTRIC
REDUCER
e. END
CLOSURE
Industry will not accept the employment of mechanics of undetermined
ability nor on the basis of past experience. Neither does industry accept
the statement that a weld is only as good as the workman who makes it.
The control Codes now in process of adoption will be the law governing
the use of the welding process. These Codes prohibit individual practices
contrary to their specified procedure and rules of control, and this is
predicated upon the sound requirement that the employer must assume
full responsibility for the deposited weld.
It is advisable that this management responsibility be included in all
welding specifications and that authoritative standards of workmanship
also be specified. The standards of workmanship for this industry are as
set forth in the Standard Manual on Pipe Welding of the Heating, Piping
and Air Conditioning Contractors National Association.
A complete line of manufactured steel welding fittings is now available
with plain ends machine beveled for welding and with radii similar to
short and long radius flanged fittings. Some typical types of these fittings
591
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 9. PROPOSED DIMENSIONS OF STEEL WELDING NECK FLANGES FOR
MAXIMUM STEAM SERVICE PRESSURE OF 150 LB PER SQ IN.
(GAGE) AT A TEMPERATURE OF 500 F, AND 100 LB AT 750 F
NOMINAL
PIPE
DIAMETER
OF
FLANGE
THICKNESS
OF
FLG. MIN.
DIAMETER
OP
HUB
HUB DIAM.
BEGINNING
OP CHAMPEK
R
LENGTH
THRU
HUB
DIAM. FOR
STANDARD
PIPE
DIAM. OF
BOLT
CIRCLE
No.
OF
BOLTS
SIZE
OP
BOLTS
2
3 2
4
5
6
8
10
12
14 0. D.
16 0. D.
18 O. D.
20 0. D.
24 0, D.
9
10
11
16
19
21
M
1H
2^6
32!
5% 6
7^6
12
143*
25
32
l^8
frjfe
1.32
1.66
1.90
2.38
2.88
3.50
4.00
4.50
5.56
6.63
8.63
10.75
12.75
14.00
16.00
18,00
20.00
24.00
05
38
61
07
2.47
07
55
03
05
07
98
10.02
12.00
13.25
15.25
17.25
19.25
23.25
17
ISM
22%
25
4
4
4
4
4
4
8
8
8
8
8
12
12
12
16
16
20
20
H
72
All dimensions given in inches.
A raised face of ^ in. is included in thickness of flange minimum.
It is recommended that the taper of the hub should not exceed 6 degrees for a reasonable distance back of the chamfer
in order to reduce the heat transfer while welding.
are shown in Fig. 1. They are made in pipe sizes ^ to 24 in., standard
and extra heavy, in steel, wrought iron, brass, copper, and special alloys.
Socket welding fittings shown in Fig. 1 are commercially available. A
proposed American Standard containing dimensions of steel welding-neck
flanges for pressures up to 1500 Ib per square inch has been developed in
A.S.A. Sectional Committee B16. Tables 9 and 10 give these dimensions
for welding-neck flanges suitable for 150 and 300 Ib per square inch
gage pressure.
VALVES
Valves are made with both threaded and flanged ends for screwed and
bolted connections just as are pipe fittings.
The material used for valves of small size is generally brass or bronze
for low pressures and forged steel for high pressures, while in the larger
592
CHAPTER 34 — PIPE, FITTINGS, WELDING
sizes either cast-iron, cast-steel or some of the steel alloys are employed.
Practically all iron or steel valves intended for steam or water work are
bronze-mounted or trimmed.
Brass, bronze, and iron valves are generally designed for standard or
extra heavy service, the former being used up to 125 Ib and the latter up
to 250 Ib saturated steam working pressure, although most manufacturers
also make valves for medium pressure up to 175 Ib steam working pres-
sure. The more common types are gate valves or straightway valves,
globe valves, angle valves, check valves and automatic valves, such as
reducing and back-pressure valves.
Gate valves are the most frequently used of all valves since in their open
position the resistance to flow is a minimum. These valves may be
secured with either a rising or a non-rising stem, although in the smaller
sizes the rising stem is more commonly used. The rising stem valve is
desirable because the positions of the handle and stem indicate whether
the valve is open or closed, although space limitations may prevent its
use. The globe valve is less expensive to manufacture than the gate
valve, but its peculiar construction offers a high resistance to flow and
may prevent complete drainage of the pipe line. These objections are of
particular importance in heating work.
Check valves are automatic in operation and permit flow in only one
direction, depending for operation on the difference in pressure between
the two sides of the valve. The two principal kinds of check valves are
the swing check in which a flapper is hinged to swing back and forth, and
the lift check in which a dead weight disc moves vertically from its seat.
Valves commonly used for controlling steam or water supply to radi-
ators constitute a special class since they are manufactured to meet
heating system requirements. These valves are generally of the angle
type and are usually made of brass. Graduations on the heads or lever
handles are often supplied to indicate the relative opening of the valve in
any position. Standard roughing-in dimensions for angle-type valves
are given in Table 11.
Automatic control of steam supply to individual radiators can be
effected by use of direct-acting radiator valves having a thermostatic
element at the valve, or near to it. The direct-acting valve is usually an
angle-type valve containing a thermostatic element which permits the
flow of steam in accordance with room temperature requirements. These
valves usually are capable of adjustment to permit variation in room
temperature to suit individual taste.
Ordinary steam valves may be used for hot water service by^drilling a
^-in» hole through the web forming the seat to insure sufficient circulation
to prevent freezing when the valve is closed. Valves made particularly
for use in hot water heating systems are of less complex design, one type
consisting of a simple butterfly valve, and another of a quick opening type
in which a part in the valve mechanism matches up with an opening
in the valve body.
In one-pipe steam-heating systems, automatic air valves are required
at the radiators. Two common types of air valves available are the
vacuum type and the straight-pressure type. Vacuum valves permit the
593
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 10. PROPOSED DIMENSIONS OF STEEL WELDING NECK FLANGES FOR
MAXIMUM STEAM SERVICE PRESSURE OF 300 LB PER SQ IN.
(GAGE) AT A TEMPERATURE OF 750 F
NOMINAL
PIPE
SIZE
DUM.
OF
FLANGE
THICK-
NESS
OP
FLANGE
MIN.
DlAM.
OF
HUB
HUB
DlAM.
BEGINNING
OP
CHAMFER
H
LENGTH
THRU
HUB
DlAM.
FOR
STANDARD
PIPE
DIAM.
FOR
EXTRA
STRONG
PIPE
DlAM.
OF
BOLT
CIRCLE
No.
OF
BOLTS
SIZE
OF
BOLTS
*2
4
5
6
8
10
12
14 0. D.
16 0. D,
18 0. D.
20 0. D.
24 0. D.
Ji
m
9
10
11
3«e
3%
&A
$H
7
15
23
28
30H
36
2M
19
21
23^
2.38
2.88
3.50
4.00
4.50
5.56
6.63
8.63
10.75
12.75
14.00
16.00
18.00
20.00
24.00
2.07
2.47
3.07
3.55
4.03
5.05
6.07
7.98
10.02
12.00
13.25
15.25
17.25
19.25
23.25
1.94
32
90
36
83
81
76
7.63
9.75
11.75
13
22^
27
32
8
8
8
8
8
8
12
12
16
16
20
20
24
24
24
*For sizes below 2 inches use dimensions of 600 Ib flanges.
All dimensions given in inches.
A raised face of fa in. is included in thickness of flange minimum.
It is recommended that the taper of the hub should not exceed 6 degrees for a reasonable distance back of the chamfer
in order to reduce the heat transfer while welding.
expulsion of air from the radiators when the steam pressure rises and, in
addition, act as checks to prevent the return of air into the radiator when
a vacuum is formed by the condensation ofsteam after the supply pressure
has dropped. Ordinary air valves permit the expulsion of air from the
radiator when steam is supplied under pressure, but when the pressure
dies down and a vacuum tends to be formed the air is drawn back into
the radiator.
A system supplied with vacuum valves will heat more quickly and
stay warm longer than one provided with straight pressure air valves;
thus it will effect considerable economy of fuel because the idle period
during which no heat is delivered is shortened. Automatic air valves are
provided with a float to close them in case the radiator becomes flooded
with water because it does not drain properly.
594
CHAPTER 34 — PIPE, FITTINGS, WELDING
CORROSION2
Corrosion is sometimes encountered in heating work on the outside of
buried pipes or the inside of steam heating systems; it is seldom ex-
perienced in hot water heating systems unless the water is frequently
renewed. Piping buried in the ground is quite successfully protected by
coatings of the asphaltic type which are usually applied hot and often
reinforced with fabric wrappings. Galvanizing by the hot-dip process and
painting with specially prepared mixtures also afford some protection.
Internal corrosion in steam heating systems occurs principally in the
condensate return pipes and is nearly always caused by oxygen or carbon
dioxide, or both, in solution in the condensate. Oxygen may enter the
heating system with the steam, owing to its presence in the boiler-feed
water, or it may enter as air through small leaks, particularly in systems
which operate at sub-atmospheric pressures. When a steam heating
system is operated intermittently, air rushes in during each shutdown
period and oxygen is absorbed by the condensate which clings to the
interior surfaces of the pipes and radiators. The rate of corrosion depends
upon the amounts of oxygen and carbon dioxide present in solution, upon
the operating temperature, and upon the length of time that the pipe
surfaces are in contact with gas-laden condensate.
Another possible cause of corrosion is a flow of electric current some-
times resulting from faulty electrical circuits which should be corrected.
Electrolytic corrosion also may occur because of the presence of two dis-
similar metals, such as brass and iron, but the condensate in practically
all steam heating systems is such a weak electrolyte that this cause of
corrosion is very infrequent.
If trouble is experienced from corrosion, oxygen should be eliminated
from the feed water by proper deaeration with commercial apparatus.
The elimination of the oxygen due to air leakage is more difficult because
of the multitude of small leaks which exist around valve stems and in
pipe joints. In vacuum systems, however, an attempt should be made
to minimize such leakage.
Carbon dioxide in varying amounts is contained in steam produced
from the majority of water supplies. It is formed from the breaking down
of carbonates and bicarbonates which are present in nearly all natural
waters. It can be partly removed by chemical treatment and deaeration,
but there is no simple method whereby it can be entirely eliminated.
These gases cause corrosion only when in solution in the condensate;
when they are mixed with dry steam their corrosive effect is negligible.
The amount of gas in solution depends upon the partial pressure of that
gas in the atmosphere above the surface of the solution, in accordance
with the well known physical law of Henry and Dalton8. The exact
application of this law, however, assumes equilibrium conditions which
do not always exist under the flow conditions prevailing in a heating
system.
*New Light on Heating System Corrosion, by J. H. Walker (Heating and Ventilating, May, 1933).
"Some Fundamental Considerations of Corrosion in Steam and Condenaate Lines, by R. E. Hall and
A. R. Mumford (A.S.H.V.E. TRANSACTIONS, Vol. 38, 1932).
595
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Distinction should be made between corrosion in heating systems proper
and in the condensate discharge lines from other apparatus using steam,
such as water heaters, kitchen equipment, and sterilizers. Experience
has shown that in heating systems the partial pressures of the gases do
not reach such magnitudes as to cause harmful amounts of gas to become
dissolved in the condensate when steam supplies are of reasonable purity.
In other kinds of steam-using apparatus which are not ordinarily well
vented, the gases tend to accumulate in the steam space and to become
dissolved in the condensate' in appreciable concentrations. Consequently,
corrosion is frequently observed in the condensate discharege lines from
such apparatus, but this does not necessarily indicate that equally serious
corrosion is taking place in the heating system supplied with steam from
the same source.
TABLE 11. STANDARD ROUGHING-IN DIMENSIONS ANGLE TYPE VALVES
SIZE
OF
VALVH
DIMENSION A
STEAM AND
Hor WATER ANGLE VALVES
AND UNION ELBOWS
EFFECTIVE JANUARY 1, 1926
DIMENSION A
MODULATING VALVES
EFFECTIVE JANUARY 1, 1926
DIMENSION A
RETURN LINE VACUUM
VALVES EFFECTIVE
JANUARY 1, 1925
1 4
3 4
2$t
3
?*
2
Tolerance
3H
3j|
All dimensions given in inches.
Connecting ends shall be threaded and gaged as to threading according to the American (Taper) Pipe Thread Standard,
A.S.A. No. B2—1919.
The standardization of the Roughing-in Dimensions of Angle Steam and Hot Water, and Modulating Radiator Valves was
made possible by the cooperation of the Manufacturers Stanaardiaation Society of the Valves and Fittings Industry.
When corrosive conditions are believed to exist, their seriousness should
be determined by actual measurement, rather than by inference from
isolated instances of pipe failures. The National District Heating Associa-
tion has perfected a corrosion tester for measuring the inherent corrosive-
ness of existing conditions. This corrosion tester consists of a frame sup-
porting three coils of wire which are carefully weighed. After the tester
has been inserted in the pipe line for a definite length of time, the loss of
596
CHAPTER 34 — PIPE, FITTINGS, WELDING
weight of the coils, referred to an established scale, indicates the relative
corrosiveness of the condensate. Accompanying such corrosion measure-
ments, a careful chemical analysis should be made of the condensate, and
the findings will serve as a basis for an intelligent study of the problem.
Corrosion, if found to exist, can be lessened or overcome by several
means. If the steam supply is found to be definitely contaminated,,
proper chemical treatment of the water, followed by deaeration, is an
obvious remedy. The leaks in the piping system, particularly in vacuum
systems, should be stopped so far as is practicable.
Some success has been reported with the use of inhibitors, chief among
which are oil, sodium silicate, and ammonia. Oil may be fed into the
main steam-supply pipe by means of a sight-feed lubricator. The type of
oil known as 600- W is usually recommended. In the present state of
knowledge on this point, the quantity to be fed can best be determined by
trial. The use of sodium silicate, fed in a similar manner, is reported to
be successful but it has not been widely used.
The effect of ammonia is to increase the pH value of the condensate
above the point where corrosion is likely to take place. Speller4 reports
having injected small quantities of ammonia into a small closed heating
system (the entire amount of condensate being returned to the boiler) and
finding the pH value maintained at a high point for several months
without further additions of ammonia. The concentration of ammonia
must be kept low to avoid corrosion of brass parts of the system. The use
of ammonia is not to be recommended where steam may come in contact
with food or other materials.
In view of the fact that corrosion is most frequently found in the
return lines from special equipment, which constitute a relatively small
part of the total piping in a building, a simple solution of the corrosion
problem may be to use non-corroding materials in those certain portions
of the piping system, since the higher cost will usually be an unappreciable
portion of the total. Brass and copper are undoubtedly less subject to
this type of corrosion than the ferrous metals, and considerable attention
is now being given to corrosion-resistant linings for ferrous pipe. Cast-
iron pipe, sometimes alloyed with other metals, also deserves con-
sideration.
^Corrosion in Steam Heating Systems, by F, N. Speller (A.S.H.V.E. TRANSACTIONS, Vol. 34, 1928).
PROBLEMS IN PRACTICE
1 • What materials are used for pipes of heating systems?
Steel pipe is generally used for steam piping and for return lines where corrosion is not
particularly active. Where corrosion is an important factor, it is good practice to use
special corrosion-resistant ferrous alloys, or brass or copper pipe.
2 • Why is thin-walled copper pipe made up with sweated joints?
If the pipe were threaded it would be necessary to use at least standard-weight wall
thickness on account of the metal removed in threading. Flared ends with coupling nuts
may be used, but this construction is expensive and hard to keep tight.
597
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
3 • How are pipes designated in diameters of 12 in. and less?
By weight and nominal size, referring to the approximate inside diameter.
4 • How are pipe sizes designated in diameters of 14 in. and more?
By wall thickness and outside diameter.
5 • Why are expansion joints required in steam pipes?
To care for the change in length of the line brought about by a change in temperature,
6 • What devices are used for taking up expansion?
Expansion joints, swivel joints, and the inherent flexibility of the pipe itself.
7 • Where are swivel joints principally used?
In branch connections to radiators, and in the risers of multi-story buildings where they
are installed between the floor joists.
8 • Name three grades of American Standard screwed pipe fittings.
125-lb cast-iron, 150-lb malleable iron, and 250-lb cast-iron.
9 • In wfyat sizes are American standard cast-iron flanges and flanged fittings
for 25-lb saturated steam pressure made?
In nominal sizes from 4 in. to 72 in., inclusive.
598
Chapter 35
WATER SUPPLY PIPING
Maximum Possible Flow, Maximum Probable Flow, Average
Probable Flow, Factor of Usage, Kind of Pipe Used, Sizing of
Risers, Sizing of Mains, Sizing of Systems, Hot Water Supply,
Hot Water Storage
DOMESTIC water supply systems present the engineer with a design
problem that requires combining the somewhat empirical rules and
formulae in use with the more or less exact hydraulic principles involved.
Unlike heating and ventilating layouts, there are practically no definite
data for estimating the quantity of water likely to be consumed or the
probable rate of water flow at any particular moment.
Metered resujts in one building often show two or three times the
metered amount in another building of the same size and with the same
type of tenants. In hotels, one riser will often have an almost constant
flow that may never be reached by another at peak load. In office
buildings, the women's toilets show a far greater daily consumption than
those of the men, yet at no time will they approach the hourly consump-
tion of the men's toilet during the first hour of the day. This condition
has led to a multiplicity of rules of practice which vary as much as the
data used. All must of necessity be based on an assumed rate of con-
sumption and on an assumed probability of simultaneous use, and while
the formulae employed may have been derived on sound technical bases
the assumptions are often in error.
To arrive at a safe standard, the approximate rate of flow of each
fixture to be supplied must be known and the probable number of fixtures
in use at any one time must be assumed. Obviously, the maximum
number of fixtures assumed to be in use must be taken at the peak of
demand and the lines must be made adequate to supply such a peak
regardless of the riser or branch on which the demand may occur. This
means that all water piping under the usual conditions will be over-sized.
In tall buildings it is customary to divide the water supply systems,
both hot and cold, into sections of 10 to 20 stories. Such zoning or
sectionalizing is for the purpose of avoiding excessive pressures on the
fixtures in the lower stories of each system. This limits the consideration
of water pipe sizes to horizontal mains and to risers not exceeding 20
stories in height or about 200 ft1.
lit Is impractical to attempt to size piping so as to produce the proper pressure on fixtures at different
levels by employing friction, owing to the fact that this friction will be built up to the amount desired only
in times of maximum demand and at all other times the friction will be only a fraction of the maximum
friction so that the fixtures by this method are subjected to a varying pressure on the water supply line. A
much more practical method is to throttle the flow at the fixture, or to use flo-w regulators, so that the
quantity of water delivered will approximate the fixture demands and so that this is accomplished without
splashing or noise,
599
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
For the purpose of this chapter the following terms will be used and
should be clearly distinguished from one another:
Maximum Possible Flow: The flow which would occur if the out-
lets on all fixtures were opened simultaneously. This condition is seldom,
if ever, obtained in actual practice except in cases of gang showers con-
trolled from one common valve, and similar conditions.
Maximum Probable Flow: The maximum flow which any pipe is
likely to carry under the peak conditions. This is the most important
amount to be considered in pipe sizing.
Average Probable Flow: The flow likely to be required through the
line under normal conditions.
It is evident that any pipe adequate to take care of the maximum
Maximum Probable Percentage of Use
*— N> u> -t* en a* ^ oo UD c
oooo ooo^ooc
y
\
\
N
\
\
\
s,
ss
\
""-^
n
•*»^
ia
^
s.
--y.
2j
iures_^
11^.
— -
— .
X
"*•
""•i
^t
'3/1
rfi
xtu
m
1<
?J
fr-tf-
,2%
-44-
^
^c
I 2 345 8 10 20 30 40 50 80 100 200 500 1000
Number of Fixtures
FIG. 1. CHART SHOWING RELATION BETWEEN NUMBER OF FIXTURES AND
MAXIMUM PROBABLE PERCENTAGE OF USE
probable flow will also be more than able to take care of the average
probable flow, and hence the latter has no bearing on the pipe size,
MAXIMUM PROBABLE FLOW
There are two factors to be considered in calculating the maximum
probable flow, namely, (1) the quantity of water that will flow from the
outlets when they are open, and (2) the number of outlets likely to be open
at the same time. Table 1 shows the maximum approximate rate of flow
from each fixture when it is in use, and will serve as a guide in estimating
maximum probable flow demands although there is considerable variation
in different fixtures and valves. Probably the flow under normal water
pressures, or with the pressure properly throttled, will not differ greatly
from the values stated. With the aid of this table it is possible to calculate
the maximum possible, flow with all outlets open in both the hot and cold
water lines.
600
CHAPTER 35 —
SUPPLY PIPING
Factor of Usage
To obtain the maximum probable flow it is necessary to multiply the
maximum possible flow by a factor of usage, and this factor varies with the
installation and the number of fixtures in the installation. It is evident
that with two fixtures it is quite possible that both will at some time be in
operation simultaneously. With 200 fixtures, it is unlikely the entire
200 would ever operate at the same time. Consequently, the factor of
usage reduces as the number of fixtures becomes greater, all other things
being equal. On the other hand it is probable that outside of flush valve
TABLE 1. APPROXIMATE FLOW FROM FIXTURES UNDER NORMAL WATER PRESSURES
FIXTURES
COLD WATER
(GALLONS PER
MINUTE)
HOT WATER
(GALLONS PER
MINUTE)
Watsr-closets, flush valve .
50 a
0
Water-closets, flush tank
18
0
Urinals, flush valve
40 a
0
Urinals, flush tank
18
0
Urinals, automatic tank . .
1
0
Urinals perforated pipe per foot
10
0
Lavatories
3
3
Showers, 5 to 6 J^ in. heads
3
3
Showers, tubular * . ... .
6
6
Needle bath
30
30
Shampoo sorav
1
1
Liver spray
2
2
Manicure table .
1H
1H
Baths, tub
5
5
Kitchen sink .
4
4
Pantry sink, ordinary
2
2
Pantry sink, large bibb
6
6
Slop sinks
4
4
Wash travs . ..
3
3
aActual tests on water-closet flush valves indicate 40 gpm as the maximum rate of flow with 30 Ib pres-
sure at the valve; this would increase to 60 gpm (about 50 per cent) at 90 Ib pressure. The 50 gpm has been
taken as an average flow; possibly, with very low pressures just sufficient to operate the flush valve, 30 gpm
could be allowed with safety. Urinal flush valves would vary proportionately in the same manner.
fixtures, the factor of usage would never be less than about 25 per cent no
matter how many fixtures were installed, provided no fixtures in excess of
those required for the actual occupancy were included.
This factor, beginning at 100 per cent for two ordinary fixtures,
decreases rapidly until 5 fixtures are reached and then becomes almost
constant, as shown in the upper curve, Fig. 1. This applies to a normal
building and not to institutions where the inmates may all be required,
for instance, to bathe on certain days of the week and at certain hours of
those days. In such special cases a new factor of usage must be developed
based on the maximum probable usage under the conditions ^involved.
For flush valve fixtures the quantity of water is greater, but owing^to the
short duration of the flush, the simultaneous usage drops more rapidly sc
as to reach 1 per cent for 1000 fixtures as shown, on lower curve, Fig. I2,
*This can be proved by assuming, for example, 1000 water-closets which would not be used more that
six times per hour (or once every 10 minutes) and which require from 5 to 7 gal per flush or an average o
about 6 gal. If these closets were all being used at their utmost capacity, the water demand would b<
600 gpm. But average use would be about one-third of this and peak conditions would be in the neigh
borhood of twice the average, or about 400 gpm as the maximum that would ever develop. Assuming 5(
gpm as the maximum rate of flow per closet and 1 per cent of the total closets in operation, the rate wouk
be 50 gpm X 1 per cent of 1000 or 500 gpm, This is 100 gpm higher than obtained by the first method
Indicating an additional factor of safety over the first method.
601
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Example 1 . Assume that in a normal building, such as a residential hotel or an apart-
ment house, there are 50 flush valve water-closets, 50 lavatories, 50 sinks and 50 baths,
and that it is desired to determine the maximum probable flow in a line supplying all of
these fixtures with both hot and cold water. Fig. 1 shows a maximum probable use for
50 water closets of about 8 per cent and for 150 ordinary fixtures, of about 31 per cent.
Therefore:
Cold Water
50 W. C, x 50 gpm at 8 per cent 200 gpm
50 Lavs, x 3 gpm 150 gpm
50 Sinks x 4 gpm 200 gpm
50 Baths x 5 gpm 250 gpm
150 Fixtures 600 gpm at 31 per cent 186 gpm
Total maximum probable flow of cold water 386 gpm
Hot Water
50 W. C , None
50 Lavs, x 3 gpm _ 150 gpm
50 Sinks x 4 gpm 200 gpm
50 Baths x 5 gpm 250 gpm
150 Fixtures 600 gpm at 31 per cent 186 gpm
Total for main supplying cold and hot water 572 gpm
It should be noted that this is a rate of flow or an instantaneous demand.
KIND OF PIPE USED
Before entering into the actual sizing of pipe, it is necessary to consider
the kind of pipe to be used, and to make suitable allowance for corrosion
and fouling during the lifetime of the system. For example, if brass,
copper or alloy pipe is contemplated, it is probable that the quantities
indicated in Example 1 are ample; if galvanized pipe is to be used, then it
is quite likely that after a period of say 15 years the area may be decreased
as much as 25 per cent and the quantitities of water assumed should be
increased by 35 per cent to allow for this reduction of area; if the water
contains lime it is possible that 50 per cent of the area may be lost and in
such cases the flow should be doubled and no branch pipe connected to
fixtures should be less than % in. In all of the following calculations, the
assumption is made that the water is fairly good and that a corrosion
resistant type of pipe is to be used.
SIZING A DOWN-FEED RISER
Down-feed systems are commonly used for tall buildings. In sizing a
riser arranged for down-feed, the gravity head permits a pressure drop
that is almost prohibitive in an up-feed risen There is a gain in riser head
of 0.43 X 100 or 43 Ib per 100 ft of run and hence it is quite permissible
to size such a riser on the basis of a pressure drop of 30 Ib per 100 ft of run,
as the difference between the 43 Ib generated and the 30-lb drop under
maximum probable demand is ample to take care of the friction caused by
602
CHAPTER 35 — WATER SUPPLY PIPING
the fittings. This method applied to the typical riser shown in Fig. 2
gives the schedule of sizes indicated in Table 2 for any flow from 5 to 250
gal.
CO CO CO CO CO CO
CO CO CO CO CO
COCO CO COCO COCO COCO
CO CO CO
COCO CO COCO COCO COCN
CO CO - CO CO CO
CO CO CO
CO COCOCO tN CO CO CN CO CO
CO CO CO CO (N CO CO
CO CO CO CO CO
COCO CO COCO COCO COCO
I iH iH
Pi"'
hcoftsOBsQ^^^^^^^^k*
tf
go
«s
*g
cccccccifcEc^^^^^^EE^jS
§fg|Sg**i§g§|£|£:B£SSl3o
t't't tttttttt tut mitEi
6n ' '^ ' 'ft} "O1 ' ' P- ' ' O ^ighj^^^&JO^^QOfiQ-^ Q
(NtN
Is
SIZING AN UP-FEED RISER
When the riser is an up-feed, the opposite condition occurs; that is,
there is a drop in pressure as the top of the riser is approached, due to the
natural reduction in the gravity pressure, and to this must be added the
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
pipe friction plus that introduced by the pipe fittings, all of which produce
an excessive drop when compared to the conditions existing with a down-
feed riser.
To size an up-feed riser the minimum pressure of the street main, or
other source of supply, should be ascertained and from this should be
subtracted the pressure to be maintained at the highest fixture, namely,
15 Ib per square inch, plus the height in feet above the source of water
pressure, multiplied by 0.43 to change from feet of head to pounds of
pressure. The total length of run from the source of pressure to the
farthest and highest fixture should be ascertained, and this should be
changed to equivalent length of run to allow for the loss occasioned by
the pipe fittings. Table 3 gives the additional lengths necessary to allow
for the various fittings and valves. The drop allowable in pressure per
100 ft of run may then be obtained by multiplying the surplus pressure
(over that required for the gravity head and to supply 15 Ib at the fixture)
by 100 and by dividing this by the equivalent length of run to the farthest
or highest fixture.
Example 8. Assume a street pressure of 60 Ib, the height of the highest fixture 50 ft,
and the length of the longest run 200 ft. Without knowing the additional length of pipe
to be added for the fittings it will be assumed that this is about 100 ft. The surplus
pressure which will be available for pressure drop will then be
60 Ib - (15 Ib + 50 ft X 0.43 Ib) =
60 Ib - (15 Ib + 21.5 Ib) = 23.5 Ib
To change this into drop per 100 ft:
23.5 Ib X 100
200 ft + 100 ft
7.8 Ib per 100 ft.
The pipe may then be sized from the maximum probable flow by selecting a size that
does not give a drop in excess of 7.8 Ib per 100 ft.
It will be seen from Example 2 that it is impossible to size up-feed
risers without determining the drop allowable in both the horizontal feed
mains and the toilet room branches. Having once ascertained this allow-
able drop, it is simply a matter of applying it throughout the system.
TABLE 3.
APPROXIMATE ALLOWANCES FOR FITTINGS AND VALVES
IN FEET OF STRAIGHT PIPE
TTPE or FITTING OR VALVE
SIZE OF PIPE
(INCHES)
90-Deg
Elbow
45-Deg
Elbow
Return
Bend
Gate
Valve
Globe
Valve
Angle
Vafve
K
4
3
8
2
48
8
H
5
3
10
3
60
10
l
5
3
10
3
60
10
IK
6
4
12
3
72
12
IX
7
5
14
4
84
14
2
7
5
14
4
84
14
m
10
7
20
5
120
20
3
12
8
24
6
144
24
4
18
13
36
9
216
36
5
25
18
50
13
300
50
6
30
21
60
15
360
60
604
CHAPTER 35 — WATER SUPPLY PIPING
HORIZONTAL SUPPLY MAINS
The horizontal mains supplying the risers at the top of a down-feed
system must be liberally sized unless the house tank is set at a much
higher elevation than usual. To provide a gravity head on the highest
fixtures of 15 Ib per square inch it is necessary for the water line in the
house tank to be nearly 40 ft higher, and with the line loss considered this
becomes about 45 ft. Such heights are not often practical and as a result
the pressure on the highest fixtures either is reduced to 7 Ib (which is
sufficient to operate a flush valve), or flush tank water-closets are sub-
stituted, or a separate cold and hot water supply is installed with a small
pneumatic tank to give the increase in pressure necessary. The chief
objection to the use of a pneumatic tank is that a separate hot water
heater is required and this heater must be located either sufficiently
below the highest fixtures to obtain a gravity circulation, or it must be
provided with a circulating pump in order to force the hot water to the
top floor level.
The most common solution is to place the house tank as high as the
structural and architectural conditions will permit and then to use
liberally-sized lines between the house tank and the upper fixtures, say for
the two top stories, below which the riser sizes may be reduced to those
indicated in Fig. 2 and Table 2. Where the house tank is only one story
above the top fixtures, flush tank water-closets must be used and the
drop in the entire run from the house tank down to the farthest fixture
should not exceed 1 Ib ; the less, the better. This means that if the total
equivalent run to the farthest top fixtures supplied is 300 ft, the drop per
100 ft should not exceed 1 lb * 1Q° or 0.33 Ib per 100 ft. The friction
oUU
curves shown in Fig. 3 may be used for quickly determining the proper
size of pipe to give any desired drop in pounds per 100 ft of equivalent run.
OVERHEAD DISTRIBUTION MAIN
Example 3. Suppose an installation has a house tank in which the water line is 20 ft
above the level of the top fixtures to be supplied and that the length of run to the
farthest fixtures on this level is 400 ft with the pipe fittings adding another 200 ft,
making an equivalent length of 600 ft. What would be the size of main coming out
of the tank where a maximum flow rate of 400 gpm may be expected, of the horizontal
main where a maximum flow rate of 200 gpm may be expected, and of the riser down to
the fixture level where the maximum flow rate is approximately 100 gpm?
Here the level of the water in the house tank is 20 ft above the faucet of the highest
fixture and the gravity pressure will be
0.43 Ib X 20 ft « 8.6 Ib
and, if a total pressure drop of 1 Ib is assumed, the pressure on the farthest fixture under
times of peak load will be
8.6 Ib - 1 Ib - 7.6 Ib
while the drop per 100 ft of equivalent run will have to be
Hb X 100
600
« 0,1667 Ib.
Referring to Fig. 3 it' will be noted that where the flow through the main is 400 gpm, ^an
8 in. pipe would be required; that where the flow is reduced to 200 gpm, a 6-m. pipe
605
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
would be sufficient ; and that where the flow is 100 gpm in the riser branch and riser, a
5-in. size would be correct. Of course these are somewhat excessive flows and the head
from the tank is small so that large sizes are to be expected. It would be necessary to
carry a 5-in. riser down to the branch to the top floor, then reduce to 4 in. for the
branch to the floor below the top,' and below this the sizes in Table 2 could be followed.
In such a case, flush tank closets should doubtless be substituted.
Had the tank been set 10 ft higher, the head available to be used up in friction, but
1000
900
800
700
600
500
400
a. 300
"
100
100
90
80
70
60
50
40
30
20
10
7
7\
For Clean
Iron
Pipe
VO.T 0.2 0.3 0.4 0.5 1.0 2.0 3.0 4.0 5.0 10 20 30 40 50 100
Friction Loss per 100 Ft Straight Pipe in Pounds per Square Inch
Fro. 3, CHART GIVING FRICTION LOSSES FOR VARIOUS RATES OF FLOW OF WATER
still giving th^same pressure at the top fixtures, would have been 0.43 Ib X 10 ft or 4.3 Ib
greater and this, with the 1 Ib drop used previously, would give a total allowable drop of
1 Ib -f 4.3 Ib = 5.3 Ib
which, divided by the 600 ft equivalent run gives a drop per 100 ft of
5.3 X 100
600
» 0.9 Ib
arid, with this drop, the sizes according to the chart (Fig. 3) are 6 in., 4 in., and 4 in,,
606
CHAPTER 35 — WATER SUPPLY PIPING
respectively, while if the run is reduced to 200 ft instead of 600 ft, the allowable drop will
be
5.3 Ib X 100
200
= 2.7 Ib per 100 ft.
This gives 5 in., 4 in., and 3 in., respectively, for the flows of 400, 200, and 100 gpm.
Water Line
n
h
House Supply
„•
^
Fire Reserve
House Tank-!"'
*
•- " -—
j
r
~2
*
5"
' 199 4" '
296
5"
297
199
4"
4W.C.-F.V.
2U.-F.V. 202
3 Lav.
•4"
6W.C.-F.V
4 Lav.
137
3"
IS. S.
8th.
4->-
+-V-
179
2*'
4W.C.-F.V.
2U.-F.V. 189
3 Lav.
«f
6W.C.-F.V.
4 Lav.
136
2f
1S.S.
7th. :
h- >•
1— >•
I1 — >•
165
2"
4W. C.-F.V.
2U.-F.V. 182
3 Lav.
2"
6W.C.-F.V.
4 Lav.
134
2"
1S.S.
6th.
*— ^-
t—^-
*— *•
134
2"
4W.C.-F.V.
2U.-F.V. 173
3 Lav.
2"
6W. C.-F.V.
4 Lav.
133
2"
1S.S.
5th.
• ^
I 3^
4W.C.-F.V.
3W.C.-F.V.
19
1"
10 Lav. 164
2"
2U.-F.V.
131
2"
ILav.
3 Lav.
1S.S.
4th. J
*— ^
:«— **
*-*•
10
r
1S.S. 149
2"
4W. C.-F.V.
2U.-F.V.
129
2"
2 Lav.
3 Lav. '
3rd. .
>— >•
*-*-
8
i"
1 S, S. 98
4'
2W.C.-F.V.
1U.-F.V.
ILav,
127
2"
3W.C.-F.V.
ILav.
2nd.
it— >•
i— *•
,i >
4
4
!.— a^
1 S. S., 50
«— *^
1WC.-F.V.
4
r
i -,w
1S.S.
1st
(1\ (2) (3)
FIG. 4, TYPICAL LAYOUT FOR DOWN-FEED SYSTEM
From Example 3 it is evident that, while the down-feed system possesses
certain economies in size for the riser portion, it is quite likely to involve
large distribution main sizes, especially when the tank is not elevated to a
considerable degree.
SIZING A PIPING SYSTEM
Example 4> Fig. 4 shows a typical layout with three risers extending eight stories arid
with the fixtures noted on each floor. First this will be solved for a down-feed arrange-
ment assuming that the level of the water in the house tank is 30 ft above the fixtures on
607
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
the top floor, that the length of run from the tank to the farthest fixture is 200 ft, equiva-
lent length of fittings 100 ft, and the pressure required at the fixture is 7 Ib.
The 30-ft head is equal to a static pressure of 0.43 X 30 or 12.9 Ib per square inch and
to maintain a pressure of 7 Ib at the highest fixtures the drop allowable in pressure is
12.9 - 7.0 Ib or 5.9 Ib. As the total equivalent run is 300 ft, this is a drop per 100 ft of
1.97 Ib, or practically 2 Ib. Therefore, all risers and mains from the top floor back to the
TABLE 4. TYPICAL CALCULATION OF PIPE SIZES ON DOWN-FEED RISER WITH
FLUSH VALVE WATER-CLOSETS AND URINALS
Riser No. 1. (See Fig. 4)
FLOOR
OF
BLDG.
FIXTURES
ON
FLOOR
GPM
PER
FIXTURE
MAXIMUM
FIXTURES
GPM
PROBABLE
USE
(PER CENT)
PROBABLE
FIXTURES
GPM
PROBABLE
RISER
GPM
ALLOWABLE
DROP
LB PER 100 FT
PIPE
SIZE
IN.
1st
1 S. S.
4
4
100
4
4
30
H
2nd
1 S. S.
4
4
100
4
8
30
%
3rd
1 S. S.
4
4
3
12
80
10
10
30
H
4th
10 Lav.
3
30
13
42
45
19
19
30
I
5th
4 W. C.
2U.
50
40
200
80
6
3 Lav.
3
280
9
40
112
16
51
45
22
134
30
2
6th
4 W. C.
2 U.
50
40
200
80
12
3 Lav.
3
560
9
25
140
19
60
42
25
165
30
2
7th
4 W. C.
2U.
50
40
200
80
18
3 Lav.
3
840
9
18
151
22
69
40
28
179
30
2M
8th
4 W. C.
2U.
50
40
200
80
24
3 Lav.
3
1120
9
15
168
25
78
40
31
199
2
4
tank must be sized on the basis of a drop of 2 Ib per 100 ft. Tables 4,5,6 and 7 show the
schedule for Risers No. 1, 2 and 3 with the maximum possible flow taken from Table 1,
the percentage of use at the peak taken from Fig. 1, and the maximum probable flow at
the peak worked out for each portion of the riser, the riser sizes being taken from Table 2
as far as possible and from Fig. 3 where the amounts exceed the values given in this
table; a drop of 30 Ib per 100 ft is used except on the riser from the top floor back to the
tank where 2 Ib per 100 ft is the allowable limit.
The reduction in pipe size which would occur if flush tank water-closets were used on
the top floor and only 3 Ib pressure used on the fixtures is given in Tables 8 and 9.
608
CHAPTER 35 — WATER SUPPLY PIPING
This illustrates why flush tank closets so frequently are substituted on the uppermost
floor when a house tank is the source of water pressure.
If it is now assumed that Riser No. 1 is to be fed from the bottom and the minimum
street pressure is 75 Ib with the top fixture of the riser 80 ft above the main, the problem
TABLE 5. TYPICAL CALCULATION OF PIPE SIZES ON DOWN-FEED RISER WITH
FLUSH VALVE WATER-CLOSETS AND URINALS
Riser No. 2. (See Fig. 4)
FLOOR
OF
BLDG.
FIXTURES
ON
FLOOR
GPM
PER
FIXTURE
MAXIMUM
FIXTURES
GPM
PROBABLE
USE
(PER CENT)
PROBABLE
FIXTURES
GPM
PROBABLE
RISER
GPM
ALLOWABLE
DROP
LEPER 100 FT
PIPE
SIZE
IN.
1st
1 W. C.
50
50
100
50
50
30
IK
2nd
2 W. C.
1 U.
50
40
100
40
4
1 Lav.
3
190
3
50
100
95
3
98
30
1H
3rd
4 W. C.
2 U.
50
40
200
80
10
3 Lav.
3
470
9
30
141
4
12
70
8
149
30
2
4th
4 W. C.
2 U.
50
40
200
80
16
3 Lav.
3
750
9
20
150
7
21
70
14
164
30
2
5th
6 W. C.
50
300
22
4 Lav.
3
1050
12
15
157
11
33
48
16
173
30
2
6th
6 W. C.
50
300
28
4 Lav.
3
1350
12
12
162
15
45
45
20
182
30
2
7th
6 W. C.
50
300
34
4 Lav.
3
1650
12
10
165
19
57
42
24
189
30
2H
8th
0 W. C.
50
300
40
4 Lav.
3
1950
12
9
175
23
69
40
27
202
2
4
would be solved by determining the maximum rate of flow in each portion of the riser as
shown in Table 10 and then finding the allowable drop which can be used per 100 ft.
The 80 ft of riser height will use up
0.43 Ib X 80
609
34.4 Ib
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
and the pressure at the top of the required 15 Ib will make the total reduction 49.4 Ib,
leaving a balance of 25.6 Ib which may be used up in friction. If the distance from the
TABLE 6. TYPICAL CALCULATION OF PIPE SIZES ON DOWN-FEED RISER WITH
FLUSH VALVE WATER-CLOSETS AND URINALS
Riser No. 3. (See Fig. 4)
FLOOR
OF
BLDG.
FIXTURES
ON
FLOOR
GPM
PER
FIXTURE
MAXIMUM
FIXTURES
GPM
PROBABLE
USE
(PER CENT)
PROBABLE
FIXTURES
GPM
PROBABLE
RISER
GPM
ALLOWABLE
DROP
LB PER 100 FT
PIPE
SIZE
IN.
1st
IS. S.
4
4
100
4
4
30
X
2nd
3W. C.
1 Lav.
50
3
150
3
80
120
2
7
100
7
127
30
2
3rd
OW. C.
0
000
3
2 Lav.
3
150
6
80
120
4
13
70
9
129
30
2
4th
3 W. C.
50
150
6
ILav.
1 S. S.
3
4
300
3
4
40
120
6
20
55
11
131
30
2
5th
0 W. C.
0
000
6
1 S. S.
4
300
4
40
120
7
24
53
13
133
30
2
6th
0 W. C.
0
000
6
1 S, S.
4
300
4
40
120
8
28
51
14
134
30
2
7th
0 W. C.
0
000
6
1 S. S.
4
300
4
40
120
9
32
50
16
136
30
2H
8th
0 W. C.
0
000
6
IS. S.
4
300
4
40
120
10
36
48
17
137
2
3
street main to the bottom of the riser, which will be assumed to be the farthest one on the
horizontal line, is 100 ft, and if the fittings are sufficient to add another 100 ft, as well as
the 80 ft of vertical distance up the riser, the total equivalent run will be 280 ft, which
will be taken as an even 300 ft. Then the allowable drop per 100 ft will be
25.6 Ib X 100
300
• 8.5 Ib
and the sizes shown in Fig. 5 are based on this amount of drop. Of course the other
610
CHAPTER 35 — WATER SUPPLY PIPING
risers will have the same maximum flows at the bottom as they formerly had at the top,
namely 202 and 137 gal, respectively, for Risers No. 2 and 3. Combining these maxi-
mum flows in the same manner as pursued in the down-feed system it is seen that the
maximum flow between Riser No. 2 and Riser No. 3 is 296 gpm, and between Riser
No. 3 and the street main, 297 gpm which at a drop of 8.5 Ib gives the main sizes
indicated. It will be noted that in determining the maximum flow in an up-feed riser
TABLE 7. SIZE OF DISTRIBUTION MAIN FOR DOWN-FEED SYSTEMS (SEE FIG. 4)
RISER
No.
FIXTURES
GPM PER
FIXTURE
MAXIMUM
FIXTURES
GPM
PROBABLE
USE
(PER CENT)
PROBABLE
GPM
ALLOWABLE
DROP (Ls
PER 100 FT)
SIZE OF
MAIN
(INCHES)
16 W. C.
8U.
50
40
800
320
1
24
22 Lav.
3 S. S.
3
4
1120
66
12
15
168
25
78
40
31
199
2
4
35 W. C.
5U.
50
40
1750
200
2
64
23 Lav.
3
3070
69
8
245
48
147
35
51
296
2
5
6 W. C.
50
300
3
70
4 Lav.
6S. S.
3
4
3370
12
24
7
236
58
183
33
61
297
2
5
it is necessary to begin at the top floor and work down instead of beginning at the bottom
floor and working up as was done in the down-feed sizing.
SIZING UP-FEED AND DOWN-FEED HOT WATER SYSTEMS
Hot water supply systems, when of the circulating type, have a few
differences to be considered although the same general principles of sizing
apply to these lines as to the cold water lines. Owing to the fact that
there are no flush valves on the hot water piping and also because many
plumbing fixtures have no hot water connections, the sizes of the hot
water piping in general will be considerably less than the cold water
piping in the same building. On the other hand it is almost invariably
required that a gravity circulation be kept up in such hot water lines and
this often has a considerable influence on the size. There are three
methods of arranging circulation lines, as follow ;
1. By using the plain up-feed with a return carried back from the top of the riser and
paralleling it,
2. By carrying a supply riser up in one location thus supplying fixtures on up-feed,
then crossing over at the top and coming down past another collection of fixtures and
supplying these by a down-feed.
3. By carrying all of the water to the top of the building and dropping risers wherever
needed, feeding all hot water on a down-feed system*
611
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 8. TYPICAL CALCULATION OF PIPE SIZES ON DOWN-FEED RISERS WITH
FLUSH TANK WATER-CLOSETS AND URINALS ON TOP FLOOR ONLY (SEE FIG. 4)
FLOOR
FIXTURES
GPM
MAX.
PROBABLE
PROBABLE
PROBABLE
ALLOWABLE
PIPE
OF
ON
•PER
FlXT.
USE
USE
RISER
DROP
SIZE
BLDG.
FLOOR
FlXT.
GPM
(PER CENT)
GPM
GPM
LB PER 100 FT
IN.
Riser No. 1
7th and
below
12 W. C.
6U.
50
40
600
240
18
19 Lav.
3S. S.
3
4
840
57
12
IS
151
22
69
40
28
179
30
2^
8th
OW. C.
OU.
00
00
000
000
18
4 W. C.
2U.
3 Lav.
18
IS
3
840
72
36
9
18
151
31
186
37
69
220
3.3
4
Riser No.
7th and
29 W. C.
50
1450
below
5U.
40
200
34
1650 -
10
165
19 Lav,
3
57
42
24
189
30
2M
8th
0 W, C.
OU.
00
00
000
000
34
1650
10
165
6W. C.
18
108
4 Lav.
3
12
29
177
38
67
232
3.3
4
Riser No. 3
7th and
GW. C.
50
300
40
120
below
5S. S,
4
20
4 Lav.
3
12
9
32
50
16
136
30
2M
8th
0 W. C.
00
000
40
120
6
300
1 S, S.
4
4
10
36
48
17
137
3.3
3
612
CHAPTER 35 — WATER SUPPLY PIPING
The last method is usually the most satisfactory. (See Fig. 6.)
In the first instance the up-feed riser may be sized for the same pressure
drop as used for the cold water riser and, from the top of the riser just
below the top fixture connection, a return circulation line may be carried
back to the main return line in the basement and connected through a
check valve, set on a 45-deg angle, and a gate valve; these return circu-
lation lines should never be less than % in., and on the farther half of the
risers, not less than 1 in. to favor circulation in the far end. Typical top
and bottom connections for such risers are shown in Fig. 7.
4 W. C.-F.V.
2U.-F.V.
8th.
i*-*-
7th.
, 4 W. C.-F.V.
24 2U.-F.V.
J^ 3 Lav.
6th, :
4 W. C.-F.V.
2j 2U.-F. V.
,t 3 Lav.
5th. :
„, 4W.C.-F.V.
24 2U.-F.V.
*-*. 3LaV<
3" 10 Lav.
4th. :
H*~
3rd. :
3" 1 S. S.
2nd. :
3" 1 S. S.
3" 1 S. S,
1st :
*-»-
3" 3" Main
(I)
FIG. 5. UP-FEED
SYSTEM
For the second arrangement of hot water risers, circulation lines are
run back from the last fixture supplied to the main return circulation line
in the same manner as just described, using % in. for the near risers and
1 in. for the far risers. The sizing is much more difficult, as it is necessary
to start at the bottom floor of the return riser and work back to the top of
this riser and then carry the maximum flow across onto the top of the
corresponding supply riser and work down on this riser from the top floor
to the bottom. Naturally this gives a much greater flow in the supply
riser and aids circulation by reducing pipe friction. The allowable loss
per 100 ft in such lines must be made about half that used for the cold
613
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Vent
I!
//
-f
\
•*•
1
""*"
|
-**
I
T-.jfr_
—
II
/•?-•
(a)
(6)
(c)
FIG. 6. METHODS OF ARRANGING HOT WATER CIRCULATION LINES
water risers which do not have the combined up- and down-travel which
the hot water must make.
In the third and most common arrangement all of the water is carried
from the tank or heater directly to the top of the building and is there
distributed to the risers which are down-feed and may be sized in the
regular down-feed manner if the total equivalent run either from the
street main or house tank is taken into consideration. The return
circulation lines frorn the botton of each riser should be arranged in the
manner already outlined and any riser not going to the basement to
TABLE 9. SUMMARY OF RISER SIZES TO GIVEN MAIN SIZES (SEE FIG. 4)
RISER
No.
FIXTURES
GPM PER
FIXTURE
RISER
GPM
PROBABLE
USE
(PER CENT)
PROBABLE
GPM
ALLOWABLE
DROP (La
PER 100 FT)
SIZE OF
MAIN
(INCHES)
1
12 W. C.
6U.
50
40
600
240
18
37
151
69
18
31 Ftxt.
840
186
220
3.3
4
2
29 W. C.
5U.
50
40
1450
200
8
199
52
29 Fixt.
2490
177
00
363
33
120
319
3.3'
4
3
6 W, C.
50
300
7
33
195
131
58
10 Fixt.
2790
36
70
399
326
3.3
4
614
CHAPTER 35 — WATER SUPPLY PIPING
TABLE 10. TYPICAL CALCULATION OF PIPE SIZES ON UP-FEED RISER WITH
FLUSH VALVE WATER-CLOSETS AND URINALS (SEE FIG. 5)
FLOOR
FIXTURES
GPM
MAXIMUM
PROBABLE
PROBABLE
PROBABLE
ALLOWABLE
PIPE
OF
ON
PER
FIXTURES
USE
FIXTURES
RISER
DROP
SIZE
BLDG.
FLOOR
FIXTURE
GPM
(PER CENT)
GPM
GPM
LB PER 100 FT
IN.
Riser No. 1
8th
4 W. C.
2U.
6
3 Lav.
50
40
• 3
200
80
~280
9
40
80
112
7
119
8.5
zy*
7th
4 W. C.
2U.
50
40
200
80
12
3 Lav.
6
3
560
9
_
25
55
140
10
150
8.5
2H
6th
4 W. C.
2U.
50
40
200
80
18
3 Lav.
3
840
9
18
151
0
27
50
14
165
8.5
1\i
5th
4 W. C.
2U.
50
40
200
80
24
3 Lav.
3
1120
9
15
168
12
36
47
17
185
8.5
3
4th
24 W. C."
andU.
10 Lav.
3
1120
30
15
108
22
06
40
27
195
8.5
3
3rd
24 W. O
andU.
1 S, S,
4
1120
4
15
168
23
70
40
28
196
8,5
3
2nd
24 W. C."
andU.
IS, S.
24 ~~
4
1120
4
74
15
40
168
30
198
8.5
3
1st
24 W. C.«
andU.
is. a
4 '
1120
4
15
168
25
78
40
31
199
8.5
3
«Frora floors above.
615
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
supply fixtures must have these returns carried down to the basement
from the termination of the supply riser at whatever level it may end.
All risers, both hot and cold, should be valved at the main with an
extra check valve on the hot water return circulation so that the risers
may be cut off and repaired when necessary without disturbing the
service in the remainder of the system.
HOT WATER SUPPLY
Having designed the service hot water piping, the next step is to furnish
Top Fixture Connection and Air Vent-%
''
t
'S*
'•Return Main '-Supply Main
FIG. 7. SUPPLY AND RETURN
MAIN CONNECTIONS FOR HOT
WATER SUPPLY SYSTEM
some means of heating the water and in this respect it is necessary to pass
from the maximum probable flow to the maximum probable hourly
demand, which is quite different. If an instantaneous heater were used,
it would require adequate capacity to provide for the heating of the water
as fast as it is drawn and a heater of this type should be sized on the basis
of the maximum probable flow with the accompanying heavy drafts on
the heating device and with intervals of no draft at all. To balance these
inequalities of flow the storage-type heater is often utilized so that the
water demand can be heated during periods of light demand and stored
up for use during the periods of heavy demand. The total water con-
sumption per person usually varies between 100 and 150 gal per day when
616
CHAPTER 35 — WATER SUPPLY PIPING
laundry and culinary operations for the occupants are carried out on the
same premises. The maximum hourly demand under these conditions
will be found to be about one-tenth of the average daily consumption.
If one-third of the total water used is hot water and 125 gal per day is
assumed as a fair average of consumption per person, it is apparent that
each person uses about 40 gal of hot water per day. If one- tenth of this
represents the peak hourly load, then 4 gph must be allowed per person
for the heaviest demand. If the average occupancy of apartments is
3 persons, the peak hour demand per apartment will be about 12 gph. It
is customary to allow 10 gph of heating capacity per apartment. Water
in excess of this heating capacity drawn out during the peak hours is
provided for by storage in the hot water tank where this water is heated
during hours when the demand is below the average.
HOT WATER STORAGE
The amount of storage provided in the hot water tank or heater is
somewhat a matter of choice but is usually made ample to carry over the
peak shortage which is likely to occur and is based on the assumption that
only 75 per cent of the storage capacity will be available, as it has been
found that if more than this amount is withdrawn from storage, the tank
is so cooled down as to make the balance useless. The general rule may
be cited that the less the heating capacity the greater must be the storage,
and the greater the storage the less may be the heating capacity down to a
point where the heating capacity will fail to be sufficient to heat up the
tank storage during the periods of small load.
Example 5. A heater to supply 500 persons will have an average daily use of about
500 X 40 gal = 20,000 gal
and this is an average of
but the peak hour will require
Ho of 20,000 = 2,000 gal
and the shortage during the peak hour, if the heating capacity is made to suit the average
hourly use of 833 gal, will be
2,000 - 833 - 1167 gal
so that the storage capacity, based on 75 per cent being available from this capacity
without cooling the tank excessively, will be
1167 1KKr .
- 1556 gal
Should it be desired to reduce the size of storage tanks and to use a greater heating
capacity, it is only necessary to increase the heating capacity to say 1200 gph which then
gives
2,000 - 1200 « 800 gal
as the shortage during the peak hour, and the necessary storage will be
*$.•!?-"""+>
or the heating capacity can be increased to 1500 gal, leaving a shortage of
2000 - 1500 « 500 gal
617
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 11. ORDINARY MAXIMUM HOURLY DEMAND FOR HOT WATER FOR VARIOUS
FIXTURES IN GALLONS AND PROBABLE PERCENTAGE OF USAGE
TTPE OF
BUILDING
LAVATORIES
BATHS
SHOWEES
SLOP
SINKS
KITCHEN
SINKS
PANTRY
SINKS
FOOT
BATHS
WASH
TRAtS
Av.
MAX
USE*
Private
Public
MAXIMUM
PROBABLE
USAGE
GPM
20
20
40
300
30
30
20
20
50
Probable Usage in Per Cent of Maximum Ordinary Use
35
60
80
45
70
90
100
20
100
50
25
75
Apt. house
Club
Gym.
Hospital
Hotel
Industrial
Laundries
Office building
Baths
Residences
Schools
Y. M. C. A.
25
25
25
25
25
25
25
25
25
25
25
25
50
75
100
75
100
150
100
75
150
"75
100
33
50
100
50
50
100
150
50
166
67
67
100
33
33
100
100
33
100
100
67
67
"67
100
67
33
50
50
50
67
67
33
67
67
67
67
50
100
100
100
25
25
100
25
25
100
60
80
"so
80
100
33
33
67
50
100
100
50
50
100
60
"so
aPercentage of fixtures likely to be demanding maximum probable usage at any one time.
TABLE 12. HOT WATER CONSUMPTION IN VARIOUS TYPES OF BUILDINGS
FOR DIFFERENT PURPOSES
TYPB OF BOTLDINO
CONDITIONS
GALLONS
Hotels
Room with basin only
Room with bath
(Transient)
(Men)
(Mixed)
(Women)
Two-room suite and bath
Three-room suite and bath
10 (per day)
40 (per day)
40 (per day;
60 (per day
80 (per day
80 (per day
100 (per day
Public
Buildings
Public bath or lavatory
Public shower
Public lavatory with attendant
150 (per day per fixture) .
200 (per day per fixture)
200 (per day per fixture)
Industrial
Buildings
Per office employee
Per factory employee
Cleaning floors
2 (per day)
5 (per day)
3 (per 1000 sq ft per day)
Restaurants
S0.50 Meals
$1.00 Meals
$1.50 Meals
0.5 (per customer with hand washing)
1.0 (per customer with machine
washing)
1,0 (per customer with hand washing)
2.0 (per customer with machine
washing)
1.5 (per customer with hand washing)
4.0 (per customer with machine
washing)
618
CHAPTER 35 — WATER SUPPLY PIPING
and the storage required only
Good design requires that the heating capacity be made as small as
possible without introducing undesirable amounts of storage, as the
heating capacity directly determines the load on the source of heat.
As indicated in Example 5, the heating load is proportional to the
heating capacity and the boiler capacity must be increased for higher
heating capacities and may be reduced for smaller heating capacities with
greater storage. It may be assumed that a boiler capacity of about 3J^
sq ft3 of equivalent steam heating surface (radiation) must be provided
for every gallon of water heated 100 F or from 50 F to 150 F, which is
the temperature rise most commonly assumed and required. On this
basis it will be seen that the various conditions cited in Example 5 will
require additional boiler capacity as follows:
Heating Capacity Additional Boiler Capacity
(gph) (Sq Ft EDR)
833 2916
1200 4200
1500 5250
From this it is apparent that it is less costly to provide ample storage
and to reduce boiler capacity than to diminish the storage and supply a
greatly increased boiler capacity to compensate.
ESTIMATING HOT WATER DEMAND BY FIXTURES
In buildings where the occupancy is doubtful and only the number of
plumbing fixtures can serve as a basis for determining the probable hot
water demand, the problem is not so simple owing to the fact that a
fixture gives no information as to how heavy a service may be demanded
from the fixture and this amount of service is really the governing factor
in making an estimate of the probable hot water demand. Table 11 may
prove of some value in this respect as it gives the maximum assumed
quantity of hot water per hour which will be demanded of any fixture and
then gives a percentage of this amount which may be assumed as probable
in different types of buildings. Table 12 gives approximate hot water re-
quirements in various types of buildings.
Example 6. Let it be assumed that an apartment house with 20 apartments has 20
baths, 20 lavatories, 20 kitchen sinks and 20 laundry trays; what is the probable maxi-
mum hourly demand for hot water?
20 Baths at 40 gal and 33 per cent ..... „ ....... . ........................ . ....................... 270 gal
20 Lavs, at 20 gal and 25 per cent .......... . ................................................ .,„ 100 gal
20 Sinks at 30 gal and 33 per cent .................................... . ...... . .................. 200 gal
20 Trays at 50 gal and 60 per cent .............. . ............................................... 600 gal
Total 1170 gal
Probable peak use at one time .„ 35 per cent
Probable actual peak demand 409 gph
100 "^ ^ 3*^
'Actual requirement for 100-deg tempeiature difference — — "ZAQ ' "" ***^ 9C1 ^ per Ballon of
water heated.
519
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
If three persons are assumed to an apartment the total daily use of hot water should
approximate
20 X 3 X 40 gal = 2400 gal
and if the peak hour is 10 per cent of this amount, the peak hour by this method shows a
probable demand of one-tenth of 2400 gal, which indicates that the values in Table 7
are safe.
PROBLEMS IN PRACTICE
1 • Why is it impractical to size water supply piping so pipe friction will pro-
duce an equal pressure on each fixture?
Because the friction would be built up only in periods of maximum flow and at all other
times it would be only a fraction of that required.
2 • What is the purpose of zoning water supply systems in tall buildings?
To avoid excessive pressures in the lower stories.
3 • Define the maximum possible flow, the maximum probable flow, and the
average probable flow.
The maximum possible flow is the flow which would occur if all of the outlets on the
system were opened at one and the same time. The maximum probable flow is the flow
which will occur with probable peak conditions. The average probable flow is the flow
likely to occur under a normal condition of use.
4 • What is the factor of usage?
This is the percentage of the maximum possible flow which is likely to occur at peak load.
5 • Within what limits does the factor of usage lie?
From 100 per cent for a single fixture down to about 28 per cent for 1000 fixtures of
ordinary type, and from 100 per cent for a single fixture down to about 1 per cent for
1000 fixtures of the flush valve type.
6 • How many feet higher than the uppermost fixtures must the water line in
a house tank be to provide about 15 Ib per square inch pressure at the fixture
outlet?
Allowing for pipe losses, about 45 ft.
7 • What methods of hot water circulation commonly are employed with hot
water supply systems?
a. Upfeed risers with returns having no connections paralleling the risers.
b. Upfeed risers with returns in other locations, and with connections taken off both
supply and return.
c. One main upfeed riser, without connections, supplying all downfeed risers for all
fixtures.
ft • Which, method of hot water supply generally is the most satisfactory?
The single main upfeed riser supplying drop risers for all fixtures.
9 • How much of the water stored in a hot water storage tank really is available
for use?
About 75 per cent, because when only 25 per cent of the original water remains in the
tank it has been so cooled clown by the entering water that it is too cold for satisfactory
use.
10 • In cases of intermittent demand, does a large hot water storage tank
increase or decrease the steam load for water heating?
It decreases the steam load in cases of intermittent demand but causes no change in the
steam load if the demand is constant,
620
Chapter 36
INSULATION OF PIPING
Heat Losses from Bare Pipes, Steam and Hot Water Lines, Low Tem-
perature Pipe Insulation, Pipe Sweating, Heat Losses from Pipe
Surfaces, Thickness of Pipe Insulation, Underground Insulation
PIPE insulation performs an important function in preventing loss of
heat where steam or hot water are conveyed from one part of a
building to another, and in reducing the absorption of heat by cold pipes
as well as preventing condensation on the outer surfaces.
BARE PIPE LOSSES
Heat losses from horizontal bare iron pipes, based on data obtained
from tests conducted at the Mellon Institute, are given in Table 1. These
losses are expressed in Btu per hour per linear foot of pipe per degree
Fahrenheit difference in temperature between the steam or hot water in
the pipe and the air surrounding the pipe. The monetary value of the
loss of heat given in Table 1 may be obtained by means of Fig. 1 for
various heating system efficiencies, temperature differences, and calorific
values and costs of coal. To solve a problem, select the proper heat loss
coefficient from Table 1 and locate this value on the upper left hand
margin of the chart. Then draw lines in the order indicated by the
dotted lines, the dollar value of the heat loss per 100 linear feet of pipe per
1000 hours being given on the upper right hand scale. In using this
chart, the cost of coal should also include the labor for handling it, boiler
room expense, etc. For additional information on this subject refer to
paper entitled Heat Emission from Iron and Copper Pipe1, by F. C.
Houghten and Carl Gutberlet.
In order to determine heat losses per linear foot of pipe from known
losses per square foot, it is necessary to know the area in square feet per
linear foot of pipe. Table 2 gives these areas for various standard pipe
sizes while Table 3 gives the area in square feet for flanges and fittings
for various standard pipe sizes.
Very often, even where pipes are thoroughly insulated, flanges and
fittings are left bare due to the belief that the losses from these parts are
not large. However, the fact that a pair of 9-in. standard flanges having
an area of 3.00 sq ft would lose, at 100 Ib steam pressure, an amount oi
lA.S.H.V.B, TRANSACTIONS, Vol. 38, 1932.
021
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 1. HEAT LOSSES FROM HORIZONTAL BARE IRON PIPES
Expressed in Btu per linear foot per degree Fahrenheit difference in temperature between the
pipe and surrounding still air at 70 F
HOT WATER
STEAM
NOMINAL
PGPB
120 F
150 F
180 F
210 F
227.1 F
(SLb)
297.7 F
(50 Lb)
337.9 F
(100 Lb)
SIZE
(INCHES)
TEMPERATURE DIFFERENCE
50 F
80 F
110 F
140 F
157.1 F
227.7 F
267.9 F
Ji
0.543
0.573
0.605
0.638
0.656
0.742
0.796
%
0.660
0.690
0.729
0.762
0.781
0.886
0.955
1
0.791
0.829
0.878
0.920
0.953
1.084
1.166
1J4
0.979
1.02
1.087
1.15
1.184
1.345
1.450
1J/|
1.09
1.15
1.220
1.29
1.335
1.520
1.640
2
1.34
1.40
1.491
1.58
1.637
1.866
2.015
2y2
1.58
1.67
1.778
1.87
1.937
2.215
2.388
1.88
1.99
2.100
2.22
2.301
2.641
2.853
v/*
2.13
2.24
2.3SO
2.51
2.585
2.972
3.215
4:
2.36
2.50
2.650
2.78
2.873
3.312
3.582
4M
2.60
2.75
2.920
3.08
3.170
3.655
3.956
2.87
3.02
3.200
3.38
3.493
4.030
4.368
6
3.39
3.56
3.775
4.01
4.115
4.755
5.153
8
4.32
4.55
5.050
5.14
5.270
6.120
6.635
10
5.32
5.61
5.925
6.34
6.551
7.592
8.245
12
6.25
6.62
6.995
7.46
7.670
8.900
9.670
TABLE 2. RADIATING SURFACE PER LINEAR FOOT OF PIPE
NOMINAL
SURFACE
NOMINAL
SURFACE
NOMINAL
SURFACE
PIPE SIZE
AREA
PIPE SIZB
AREA
PIPE SIZE
AREA
(INCHES)
(SqFr)
(INCHES)
(So FT)
(INCHES)
(So FT)
y%
0.22
2
0.622
5
1.456
%
0.275
2H
0.753
6
1.734
i
0.344
3
0.917
8
2.257
iji
0.435
3M
1.047
10
2.817
i«
0.498
1.178
12
3.338
TABLE 3. AREAS OF FLANGED FITTINGS, SQUARE FEET*
NOMINAL
FLANGED
COUPLING
90 DEQ ELL
LONO RADIUS
ELL
TEE
CROSS
PIPE SIZE
(INCHES)
Standard
Extra
Heavy
Standard
Extra
Heavy
Standard
Extra
Heavy
Standard
Extra
Heavy
Standard
Extra
Heavy
1
0,320
0,438
0.795
1.015
0.892
1.083
1.235
1.575
1,622
2,07
1«
0,383
0.510
0.957
1.098
1.084
1.340
1.481
1,925
1.943
2.53
1«
0.477
0,727
1,174
1.332
1.337
1.874
1,815
2.68
2.38
3.54
2
0.672
0.848
1,65
2.01
1.84
2,16
2,54
3,09
3.32
4,06
2^
0.841
1.107
2.09
2.57
2.32
2,76
3.21
4.05
4.19
5.17
3
0.945
1.484
2.38
3.49
2.68
3.74
3.66
5.33
4.77
6.95
3^2
1.122
1.644
2.98
3.96
3.28
4,28
4,48
6.04
5.83
7.89
4
1.344
1.914
3.53
4.64
3,96
4.99
5,41
7.07
7,03
9,24
Q4
1.474
2.04
3.95
5,02
4.43
5.46
6.07
7.72
7.87
10.07
1.622
2.18
4.44
5.47
5.00
6.02
6.81
8.52
8.82
10.97
6
1.82
2.78
5,13
6.99
5.99
7.76
7.84
10.64
10,08
13.75
8
2.41
3.77
6,98
9.76
8.56
11.09
10.55
14.74
13,44
18.97
10
3,43
5,20
10.18
13.58
12,35
15.60
15,41
20.41
19.58
26.26
12
4,41
6.71
13,08
17.73
16.35
18,76
19,67
26,65
2487
34,11
•Including areaaol accompanying flanges bolted to the fitting,
622
CHAPTER 36 — INSULATION OF PIPING
FIG, 1. CHART FOR ESTIMATING DOLLAR VALUE OF HEAT Loss
FROM BARE IRON PIPES. (SEE TABLE 1)*
aThls chart is based on 100 linear feet per 1000 hours. For fractions or multiples of these factors,
multiply by proper percentage,
heat equivalent to more than a ton of coal per year shows the necessity
for insulating such surfaces. Table 3 shows the areas of both standard
and extra heavy flanged fittings including the accompanying flanges
bolted to the fittings,
STEAM AND HOT WATER LINES
The conductivities of various materials used for insulating steam and
hot water pipes are given in Table 4. In this table the conductivities are
given as functions of the mean temperatures or the mean of the inner and
623
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 4, CONDUCTIVITIES (jfe) OF VARIOUS TYPES OF INSULATING MATERIALS
FOR MEDIUM AND HIGH TEMPERATURE PipESa
MBAN TEMPERATURE
100 F
200 F
300 F
400 F
500 F
85 per cent Magnesia, Type
0.425
0.465
0.505
0.550
0.590
Corrugated Asbestos Type
0.530
0.650
0.770
0.890
.(4 Plies per 1 in. thick)
Corrugated Asbestos Type
0.480
0.555
0.630
0.705
(8 Plies per 1 in. thick)
Laminated Asbestos Type ... . .
0.360
0.415
0.470
0.525
0.585
(30-40 Laminations per 1 in. thick)
Laminated Asbestos Type
0.545
0.605
0.665
0.725
0.785
(20 Laminations per 1 in. thick)
Rock Wool Type . .....
0.350
0.410
0.470
0.530
0.590
High Temperature Type
0.515
0.545
0.575
0.605
0.635
(Diatomaceous Earth and Asbestos)
Brown Asbestos Type
0.600
0.640
0.675
0.715
0.750
(Felted Fibre)
^Mechanical Engineers' Handbook, Marks, 3rd Ed., 1930.
outer surface temperatures of the insulations. This method of stating
conductivities makes it possible readily to calculate the heat loss through
single or compound sections. It should be emphasized that the con-
ductivities given in Table 4 for the various insulations are the average of
values obtained from a number of tests made on each type of material,
also that all variables due to differences in thickness, pipe sizes, and air
conditions are eliminated. Individual manufacturer's materials will, of
course, vary in conductivity to some extent from these values.
The heat losses through six of the types of insulation given in Table 4
for 1, 1J^ and 2-in. -thick materials, and for temperatures commonly
encountered in engineering practice can be obtained from Tables 5 to 10,
inclusive. The loss through other thicknesses of the materials, and for
other hot water or steam temperature conditions may be obtained by
interpolation. The heat loss coefficients given in Tables 5 to 10 are
based on the conductivities in Table 4 and were computed from data
given in Chapter 22, THE GUIDE 1931.
LOW TEMPERATURE PIPE INSULATION
Surfaces maintained at low temperatures should be insulated so as to
retard the flow of heat from the outside into the low temperature area and
to prevent the formation of condensation and of frost if the temperatures
are low enough, as well as to prevent corrosion induced by the presence
of condensed moisture on metal surfaces. Materials commonly used for
insulating pipes and surfaces at low temperatures are cork, rock cork,
hair felt and other felted or fibrous non-absorbent materials. Thermal
conductivities of low temperature insulating materials are given in
Chapter 5.
Insulating materials are available commercially to meet varying tem-
perature gradients. For example, the thickness of insulation for ice water
is approximately 1J^ in, if the temperature in the line is not lower than
624
CHAPTER 36 — INSULATION OF PIPING
TABLE 5. COEFFICIENTS OF TRANSMISSION (U) FOR PIPES INSULATED
WITH 85 PER CENT MAGNESIA TYPE INSULATION
These coefficients are expressed in Btu per hour per square foot of pipe surface per degree
Fahrenheit difference in temperature between pipe and surrounding still air at 70 F
HOT WATER STEAM
THICKNESS
NOMINAL
II
OF
INSULATION
PIPE
SIZE
120 F
1SOF
180 F
210 F I 22 VJ
1 (5 Lb)
297.7 F
(50 Lb)
337.9 F
(100 Lb)
(INCHES)
(INCHES)
TEMPERATURE DIFFERENCE
50 F
80 F
110 F
140 F
157.1 F
227.7 F
267.9 F
y2
0.744
0.754
0.764
0.774
0.779
0.802
0.814
H
0.672
0.681
0.689
0.697
0.701
0.721
0.731
i
0.613
0.621
0.629
0.637
0.641
0.659
0.670
U4
0.562
0.570
0.577
0.585
0.589
0.606
0.617
ix
0.532
0.539
0.546
0.553
0.557
0.573
0.582
2
0.500
0.506
0.512
0.519
0.523
0.538
0.547
11A
0.475
0.481
0.487
0.493
0.497
0.512
0.520
3
0.455
0.461
0.467
0.474
0.477
0.492
0.500
1
3H
0.441
0.447
0.452
0.458
0.462
0.475
0.483
4
0.429
0.435
0.441
0.446
0.449
0.463
0.471
4^
0.420
0.425
0.431
0.437
0.440
0.453
0.460
5
0.411
0.416
0.422
0.427
0.430
0.443
0.450
6
0.402
0.408
0.413
0.419
0.422
0.435
0.442
8
0.387
0.392
0.397
0.403
0.405
0.418
0.425
10
0.375
0.380
0.385
0.390
0.393
0.405
0.412
12
0.369
0.374
0.378
0.383
0.386
0.398
0.405
1A
0.617
0.625
0.633
0.642
0.646
0.665
0.676
H
0.550
0.558
0.566
0.573
0.577
0.596
0.606
i
0.4%
0.503
0.511
0.518
0.522
0.540
0.549
ilA
0.453
0.459
0.465
0.472
0.475
0.490
0.498
IX
0.424
0.430
0.436
0.442
0.445
0.459
0.467
2
0.394
0.400
0.405
0.410
0.413
0.427
0.434
11A
0.371
0.376
0.382
0.386
0.389
0.401
0.408
3
0.352
0.357
0.362
0.367
0.370
0.380
0.387
IX
&A
0.339
0.343
0.347
0.351
0.354
0.364
0.370
4
0.328
0.333
0.337
0.341
0.343
0.353
0.359
4M
0.320
0.324
0.328
0.332
0,334
0.343
0.350
5
0.312
0.316
0.320
0.324
0.326
0.336
0.342
6
0.303
0.307
0.311
0.315
0.318
0.328
0.333
8
0.287
0.291
0.295
0.299
0.301
0.311
0.316
10
0.276
0.280
0.284
0.288
0.290
0.299
0.304
12
0.272
0.275
0.279
0.283
0,285
0.294
0.299
X
0.543
0.551
0.558
0,565
0.569
0.587
0.597
K
0.484
0.490
0.497
0.503
0.507
0.523
0.532
0.433
0.439
0.445
0.451
0.454
0.467
0.476
11A
0.393
0.398
0.403
0.409
0.412
0.424
0.432
IX
0.365
0.370
0.376
0.381
0.384
0.397
0.402
2
0,338
0.343
0.347
0.351
0.354
0.364
0.370
2J^
0.316
0.320
0,324
0.328
0.331
0.341
0.347
3
0.297
0.301
0.305
0.309
0.312
0.321
0.326
2
3H
0.284
0.288
0.292
0.295
0.297
0.306
0.311
4
0.275
0.278
0.282
0.285
0.287
0.296
0.301
42^
0.266
0.270
0.273
0.276
0.278
0.286
0.290
0.258
0.262
0.265
0.268
0.270
0.278
0.283
6
0.250
0.254
0.257
0.260
0.262
0.270
0.274
8
0.236
0.239
0,242
0,245
0.247
0.255
0.258
10
0.224
0.227
0,230
0.233
0.235
0.242
0.246
12
0,219
0,222
0.225
0.228
0.230
0,237
0,240
625
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 6. COEFFICIENTS OF TRANSMISSION ( U) FOR PIPES INSULATED WITH CORRUGATED
ASBESTOS TYPE INSULATION (4 PLIES PER INCH THICKNESS)
These coefficients are expressed in Btu per hour per square foot of pipe surface per degree
Fahrenheit difference in temperature between pipe and surrounding still air at 70 F
HOT WATER
STEAM
THICKNESS
NOMINAL
OP
INSULATION
PIPE
SIZE
120 F
150 F
180 F
210 F
227.1 F
(5Lb)
297.7 F
(50 Lb)
337.9 F
(100 Lb)
(INCHES)
(INCHES)
TEMPERATURE DIFFERENCE
50 F
80 F
110F
140 F
157.1 F
227.7 F
267.9 F
1A
0.890
0.919
0.949
0.978
0.995
1.065
1.106
%
0.803
0.829
0.857
0.883
0.898
0.961
0.997
0.731
0.756
0.780
0.804
0.818
0.876
0.909
v/±
0.671
0.693
0.716
0.738
0.751
0.804
0.834
1H
0.635
0.656
0.677
0.698
0.710
0.760
0.788
2
0.595
0.615
0.635
0.656
0.667
0.715
0.742
2M
0.567
0.586
0.605
0.624
0.635
0.680
0.705
3
0.544
0.562
0.580
0.598
0.608
0.652
0.677
1
3J^
0.527
0.544
0.561
0.578
0.588
0.631
0.654
4
0.513
0.530
0.548
0.565
0.575
0.616
0.639
&A
0.502
0.518
0.535
0.551
0.561
0.601
0.624
5
0.490
0.507
0.523
0.539
0.549
0.588
0.611
6
0.480
0.496
0.512
0.528
0.538
0.577
0.599
8
0.462
0.477
0.493
0.508
0.517
0.554
0.575
10
0.447
0.462
0.476
0.491
0.500
0.537
0.557
12
0.441
0.456
0.470
0.485
0.493
0,529
0.550
M
0.737
0.762
0.787
0.812
0.826
0.884
0.918
%
0.657
0.679
0.702
0.725
0.737
0.790
0.820
0.594
0.614
0.634
0.654
0.666
0.713
0.740
iy*
0.542
0.5s59
0.577
0.596
0.606
0.649
0.673
m
0.507
0.524
0.541
0.558
0.568
0.609
0.632
2
0.471
0.487
0.503
0.519
0.528
0.565
0.587
%
0.443
0.458
0.473
0.488
0.497
0.533
0.553
3
0.421
0.435
0.449
0.463
0.472
0.506
0.525
1«
m
0.403
0.417
0.430
0.443
0.451
0.483
0.502
4
0.393
0.405
0.418
0.432
0.439
0.471
0.489
4H
0,383
0.394
0.407
0.420
0.428
0.460
0.476
5
0.372
0.384
0.397
0.409
0.417
0.447
0.463
6
0.362
0.374
0,387
0.399
0.406
0.436
0.452
8
0.343
0.354
0.366
0.378
0.385
0.413
0.429
10
0.328
0.339
0.351
0.362
0.369
0,397
0.413
12
0.323
0.334
0.346
0.357
0.364
0.391
0.407
H
0.648
0.670
0.692
0.713
0,726
0.779
0.810
H
0.578
0,598
0.617
0.637
0.648
0.694
0.720
1
0.518
0.535
0.552
0.570
0.580
0.622
0.645
1#
0.469
0.485
0.501
0.517
0.527
0.566
0.587
1M
0.438
0.452
0.467
0.481
0.490
0.526
0.545
2
0.404
0,417
0.430
0.444
0.452
0.483
0.502
2H
0.379
0,391
0.403
0.415
0,422
0.451
0.466
3
0.356
0.367
0.378
0.390
0.397
0.425
0.440
2
3^
0.339
0.350
0.361
0.373
0.380
0.406
0.421
4
0.328
0.339
0.350
0.360
0.367
0.392
0.406
4M
0.318
0.328
0.339
0.350
0.357
0.381
0.395
5
0.308
0,318
0.329
0.340
0.346
0.370
0.384
6
0.299
0.309
0.319
0.329
0.335
0.358
0.371
8
0.282
0.291
0.301
0.310
0.315
0.336
0.349
10
0,267
0.276
0.285
0.294
0.299
0.319
0.332
12
0,263
0.272
0,280
0.289
0.294
0,314
0.325
626
CHAPTER 36 — INSULATION OF PIPING
TABLE 7. COEFFICIENTS OF TRANSMISSION ( U) FOR PIPES INSULATED WITH CORRUGATED
ASBESTOS TYPE INSULATION (8 PLIES PER INCH THICKNESS)
These coefficients are expressed in Btu per hour per square foot of pipe surface per degree
Fahrenheit difference in temperature between pipe and surrounding still air at 70 F
HOT WATER
STEAM
THICKNESS
NOMINAL
OF
INSULATION
PIPE
SIZE
120 F
150 F
180 F
210 F
227.1 F
(SLb)
297.7 F
(50 Lb)
337.9 F
(100 Lb)
(INCHES)
(INCHES)
TEMPERATURE DIFFERENCE
50 F
80 F
110 F
140 F
157.1 F
227.7 F
267.9 F
}4
0.801
0.820
0.838
0.857
0.868
0.913
0.939
% -
0.723
0.739
0.756
0.773
0.783
0.824
0.847
1
0.658
0.673
0.688
0.704
0.713
0.751
0.772
1%
0.606
0.619
0.633
0.647
0.655
0.688
0.707
m
0.573
0.586
0.599
0.612
0.619
0.652
0.670
2
0.538
0.550
0.562
0.575
0.581
0.612
0.629
11A
0.511
0.523
0.534
0.546
0.553
0.582
0.599
3
0.489
0.501
0.512
0.524
0.531
0.558
0.575
1
3M
0.474
0.485
0.496
0.507
0.514
0.542
0.557
4
0.461
0.472
0.482
0.493
0.500
0.527
0.542
4M
0.451
0.462
0.472
0.482
0.489
0.515
0.530
5
0.442
0.452
0.462
0.473
0.479
0.505
0.520
6
0.432
0.442
0.452
0.463
0.468
0.493
0.508
8
0.416
0.426
0.436
0.446
0.451
0.475
0.489
10
0.402
0.412
0.421
0.430
0.435
0.459
0.473
12
0.397
0.406
0.415
0.424
0.429
0.452
0.466
1A
0.664
0.679
0.695
0.711
0.720
0.759
0.780
%
0.593
0.607
0.621
0.636
0.643
0.677
0.697
0.535
0.547
0.560
0.573
0.580
0.611
0,629
1M
0.488
0.499
0.510
0.522
0.528
0.556
0.572
1H
0.457
0.467
0.478
0.490
0.496
0.522
0.537
2
0.425
0.434
0.444
0.455
0.460
0.485
0.499
m
0.399
0.408
0.418
0.428
0.434
0.457
0.471
3
0.378
0.387
0.396
0.405
0.411
0.433
0.446
1H
3^
0.363
0.371
0.380
0.388
0.393
0.415
0.427
4
0.353
0.361
0.369
0.378
0.383
0.403
0.415
4^
0.343
0.351
0.360
0.368
0.373
0.393
0.404
5
0.334
0.342
0.350
0.358
0.363
0.383
0.394
6
0.325
0.333
0.341
0.349
0.353
0.373
0.383
8
0.309
0,316
0.324
0.332
0.336
0.355
0.365
10
0.295
0.303
0.310
0.318
0.322
0.340
0.350
12
0.291
0.298
0.306
0.313
0.317
0.335
0,344
H
0.585
0,599
0.613
0.627
0.635
0.668
0.688
H
0.520
0.533
0.545
0,558
0.565
0.595
0.612
1
0.465
0,476
0.487
0.498
0.504
0.532
0.547
1M
0.422
0.432
0.442
0.452
0.458
0.483
0.497
IjLg
0.394
0.403
0.412
0.422
0.427
0.450
0.462
2
0.364
0.372
0.380
0.388
0.393
0,415
0.427
2H
0.339
0.347
0.355
0.363
0.367
0.387
0.398
3
0.319
0.327
0.334
0.342
0.346
0.365
0.375
2
3M
0.304
0.311
0,318
0.326
0,330
0.349
0.358
0,295
0.302
0.308
0.315
0.319
0.336
0.345
4^
.0.285
0.292
0.299
0.306
0.310
0.327
0.336
5
0.278
0,284
0.290
0.297
0.301
0.317
0.326
6
0.269
0.275
0,282
0.288
0.292
0.307
0.315
8
0,253
0.259
0.265
0.270
0.273
0,288
0.296
10
0.240
0.245
0.251
0,257
0.260
0,275
0,282
12
0.236
0.241
0.247
0.2S3
0.256
0.270
0.277
627
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 8. COEFFICIENTS OF TRANSMISSION (£/) FOR PIPES INSULATED WITH LAMINATED
ASBESTOS TYPE INSULATION (30 TO 40 LAMINATIONS PER INCH THICKNESS)
These coefficients are expressed in Btu per hour per square foot of pipe surface per degree
Fahrenheit difference in temperature between pipe and surrounding still air at 70 F
HOT WATER
STEAM
THICKNESS
NOMINAL
OF
INSULATION
PIPE
SIZE
120 F
150 F
180 F 210 F
227.1 F
(SLb)
297.7 F
(50 Lb)
337.9 F
(100 Lb)
(INCHES)
(INCHES)
TEMPERATURE DIFFERENCE
50 F
80 F
110 F
140 F
157.1 F
227.7 F
267.9 F
H
0.605
0.620
0.635
0.650
0.658
0.695
0.716
%
0.546
0.560
0.573
0.586
0.594
0.627
0.645
i
0.498
0.510
0.522
0.534
0.541
0.570
0.587
M
0.457
0.468
0.480
0.491
0.497
0.525
0.540
VA
0.432
0.442
0.453
0.464
0.470
0.496
0.511
2
0.406
0.416
0.426
0.437
0.442
0.467
0.481
VA
0.385
0.395
0.405
0.415
0.420
0.443
0.457
3
0.370
0.379
0.389
0.398
0.403
0.425
0.438
1
m
0.359
0.367
0.376
0.385
0.390
0.413
0.426
4
0.349
0.358
0.366
0.375
0.380
0.402
0.414
4H
0.341
0.350
0.359
0.367
0.372
0.393
0.405
5
0.334
0.342
0.351
0.359
0.364
0.384
0.395
6
0.327
0.335
0.343
0.351
0.356
0.376
0.387
8
0.314
0.322
0.330
0.338
0.343
0.362
0.373
10
0.304
0.312
0.320
0.328
0.332
0.350
0.361
12
0.301
0.308
0.316
0.324
0.328
0.346
0.356
H
0.502
0.514
0.526
0.539
0.546
0.577
0.595
H
0.450
0.461
0.473
0.484
0.490
0.517
0.532
i
0.405
0.415
0.426
0.436
0.442
0.466
0.480
i#
0.369
0.378
0.387
0.396
0.401
0.423
0.435
11A
0.343
0.352
0.361
0.370
0.375
0.397
0.409
2
0.321
0.329
0.337
0.345
0.350
0.369
0.380
m
0.301
0.309
0.317
0.324
0,330
0.348
0.358
3
0.286
0.293
0.301
0.308
0.313
0.330
0.340
1H
VA
0.274
0.281
0.288
0.295
0.300
0.316
0.326
4
0.267
0.273
0.280
0.287
0.291
0.307
0.317
4K
0.259
0.266
0.272
0.279
0.283
0.299
0,308
5
0.253
0.260
0.266
0.272
0.276
0.291
0.300
6
0.247
0.253
0.260
0.266
0.269
0.284
0.293
8
0.234
0.240
0.246
0.252
0.255
0.270
0.279
10
0,223
0.229
0.235
0.241
0.245
0.258
0.266
12
0.221
0.227
0.232
0.238
0.241
0.255
0.263
1A
0.442
0.453
0.464
0.475
0.481
0.508
0.523
H
0.392
0.402
0.412
0.422
0.428
0.452
0.465
0.352
0.360
0.369
0.378
0.383
0.405
0.417
itf
0.319
0.327
0.335
0.343
0.348
0.367
0.379
IK
0.297
0.304
0.311
0.319
0.323
0,341
0.352
2
0.274
0.280
0.287
0,294
0.298
0.314
0.324
2^
0.256
0.262
0.269
0,275
0.279
0.293
0.302
3
0,243
0.249
0.254
0.260
0.264
0.277
0.285
2
3H
0.231
0.236
0.242
0.248
0.251
0.265
0.273
4
0.223
0.228
0.234
0.240
0.243
0.257
0.265
4^
0.216
0.222
0.227
0.233
0.236
0.249
0.256
5
0.210
0.215
0.220
0.225
0,228
0.241
0.248
6
0.203
0.208
0.213
0.218
0.221
0.233
0.240
8
0491
0.196
0.201
0.206
0.209
0.220
0.227
10
0.182
0.187
0.192
0.196
0.199
0.210
0.215
12
0,178
0.183
0.187
0.192
0.195
0.205
0.210
628
CHAPTER 36 — INSULATION OF PIPING
TABLE 9. COEFFICIENTS OF TRANSMISSION ( U) FOR PIPES INSULATED WITH LAMINATED
ASBESTOS TYPE INSULATION (APPROXIMATELY 20 LAMINATIONS PER INCH THICKNESS)
These coefficients are expressed in Btu per hour per square foot of pipe surface per degree
Fahrenheit difference in temperature between pipe and surrounding still air at 70 F
HOT WATER
STEAM
THICKNESS
NOMINAL,
OP
INSULATION
PIPE
SIZE
120 F
150 F
180 F
210 F
227.1 F
(5Lb)
297.7 F
(50 Lb)
337.9 F
(100 Lb)
(INCHES)
(INCHES)
TEMPERATURE DIFFERENCE
50 F
80 F
110 F
140 F
157.1 F
227.7 F
267.9 F
1A
0.910
0.925
0.940
0.956
0.964
1.001
1.022
H
0.823
0.836
0.850
0.863
0.871
0.902
0.921
i
0.748
0.760
0.773
0.785
0.792
0.823
0.840
1J4
0.686
0.698
0.710
0.721
0.728
0.756
0.771
VA
0.649
0.659
0.671
0.682
0.688
0.716
0.731
2
0.610
0.620
0.630
0.640
0.647
0.671
0.685
m
0.581
0.590
0.600
0.609
0.615
0.638
0.651
3
0.558
0.567
0.576
0.585
0.591
0.613
0.626
1
3H
0.539
0.548
0.557
0.566
0.571
0.592
0.604
4
0.524
0.532
0.541
0.551
0.556
0.577
0.589
4H
0.514
0.522
0.530
0.539
0.544
0.564
0.575
0.503
0.511
0.519
0.528
0.533
0.553
0.565
6
0.492
0.500
0.509
0.517
0.522
0.542
0.553
8
0.473
0.480
0.488
0.497
0.502
0,521
0.532
10
0.458
0.465
0.473
0.481
0.485
0.504
0.514
12
0.452
0.459
0.467
0.475
0.478
0.497
0.507
1A
0.755
0.767
0.780
0.793
0.800
0.831
0.848
H
0.674
0.685
0.697
0.708
0.715
0.743
0.759
i
0.607
0.618
0.628
0.639
0.645
0.670
0.684
U4
0.553
0.562
0.572
0.581
0.587
0.610
0.622
\1A
0,517
0.527
0.536
0.545
0.550
0.572
0.584
2
0.481
0.490
0.499
0.508
0.513
0.535
0.547
m
0.453
0,460
0.469
0.477
0.481
0.500
0.511
3
0.429
0.436
0.444
0.452
0.456
0.475
0.485-
1M
3H
0.412
0.419
0,427
0.434
0.438
0.456
0.465
4
0.400
0.407
0.415
0.422
0.426
0.443
0.453
4M
0.390
0.396
0.402
0.409
0.413
0.429
0.437
5
0.380
0.386
0,393
0.400
0.403
0.418
0.427
6
0.369
0.375
0.382
0.389
0,392
0.408
0.417
8
0.351
0.358
0.364
0.370
0,374
0.388
0.397
10
0,337
0,344
0,350
0.356
0.359
0.373
0.382
12
0.332
0.338
0.344
0.350
0.353
0.367
0,375
H
0.664
0.675
0.687
0.698
0.704
0.732
0.747
H
0.591
0.601
0,611
0.621
0.627
0.652
0.665
i
0.529
0.538
0.547
0.557
0.562
0.584
0.597
134
0.480
0.488
0.497
0.505
0.510
0.529
0.540-
IK
0.445
0.453
0.462
0.470
0.475
0.494
0.504
2
0,412
0.420
0.427
0.434
0.438
0,455
0.464
2H
0.385
0.392
0.398
0.405
0,409
0.425
0.434
3
0.364
0.370
0.376
0.382
0.385
0.400
0.408
2
3H
0.346
0.352
0.358
0.365
0.368
0.382
0.390<
4
0.336
0.342
0.348
0.354
0.357
0.371
0.378
4H
0.325
0.332
0.338
0.343
0.346
0.360
0.367
0.316
0.322
0.327
0.333
0,336
0.349
0.356-
6
0.306
0.312
0.317
0,323
0.326
0.338
0.345
B
0.288
0.293
0.298
0.303
0.306
0.317
•0.324
10
0.275
0.279
0.284
0.289
0.292
0.302
0.308
12
0.269
0.274
0.278
0.283
0.286
0.296
0.302
629
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 10. COEFFICIENTS OF TRANSMISSION (U) FOR PIPES INSULATED
WITH ROCK WOOL TYPE INSULATION
These coefficients are expressed in Btu per hour per square foot of pipe surface per degree
Fahrenheit difference in temperature between pipe and surrounding still air at 70 F
HOT WATER
STEAM
THICKNESS
NOMINAL
OF
INSIFLATION
PIPE
SIZE
120 F
1SOF
180F
210 F
227.1 F
(SLb)
297.7 F
(50 Lb)
337.9 F
(100 Lb)
(INCHES)
(INCHES)
TEMPERATURE DIFFERENCE
50 F
80 F
110 F
140 F
157.1 F
227.7 F
2673F
Ji
0.631
0.644
0.658
0.672
0.680
0.712
0.730
H
0.569
0.581
0.593
0.606
0.613
0.642
0.659
0.518
0.529
0.541
0.552
0.559
0.585
0.600
1J4
0.476
0.486
0.497
0.507
0.513
0.537
0.551
1H
0.450
0.460
0.470
0.480
0.485
0.508
0.522
2
0.422
0.431
0.441
0.450
0.456
0.478
0.490
2H
0.402
0.411
0.420
0.428
0.434
0.455
0.466
3
0.385
0.394
0.402
0.411
0.415
0.435
0.446
1
3}i
0.373
0.381
0.389
0.398
0.402
0.421
0.432
4
0.363
0.371
0.379
0.387
0.392
0.411
0.422
VA
0.355
0.363
0.371
0.379
0.383
0.402
0.413
0.348
0.356
0.364
0.371
0.376
0.394
0.404
6
0.341
0.348
0.356
0.363
0.368
0.386
0.396
8
0.327
0.335
0.342
0.349
0.353
0.372
0.381
10
0.317
0.324
0.331
0.338
0.343
0.360
0.369
12
0.313
0.320
0.327
0.334
0.338
0.355
0.364
y2
0.523
0.534
0.545
0.556
0.563
0.590
0.606
u
0.468
0.477
0.487
0.497
0.503
0,528
0.542
i
0.421
0.430
0.440
0.449
0.455
0.477
0.490
IK
0.383
0.391
0.399
0.407
0.412
0.433
0.444
i«
0.359
0.366
0.375
0.383
0.387
0.407
0.419
2
0.333
0.340
0.348
0.356
0.360
0.378
0.389
2J^
0.314
0.320
0.327
0.335
0.339
0.355
0.365
3
0.296
0.302
0.310
0,317
0.321
0.337
0.347
1H
m
0.286
0.291
0.298
0.304
0.307
0.323
0.332
4
0.278
0.284
0.290
0.296
0.300
0.315
0.323
4^
0.270
0.276
0.282
0,287
0.291
0.305
0,313
5
0.263
0.269
0.275
0.280
0.284
0.298
0.305
6
0.257
0.262
0.267
0.273
0.277
0.290
0.297
8
0.244
0.249
0.254
0.260
0.263
0.276
0.283
10
0.235
0.240
0.245
0.250
0.253
0.265
0.272
12
0.230
0.234
0.239
0.245
0.247
0.260
0.267
«
0.461
0.471
0.481
0.491
0,496
0.520
0.534
«
0.409
0.418
0.427
0.436
0,441
0.463
0.475
0.366
0.374
0.382
0.390
0.395
0.415
0.427
IK
0.333
0.340
0.347
0,355
0.359
0.377
0.387
1«
0.310
0.316
0.323
0.330
0.334
0.351
0.360
2
0.286
0.292
0.298
0.304
0.308
0.323
0.331
2M
0.268
0.274
0.279
0.285
0.289
0.302
0,310
3
0.252
0.257
0.262
0.268
0.272
0.284
0.292
2
m
0.241
0.246
0.251
0.257
0.260
0.272
0,280
4
0.232
0.237
0.242
0.247
0.250
0.262
0,269
4H
0.225
0.230
0.235
0.240
0.243
0.255
0,262
5
0.218
0.223
0.228
0.233
0.236
0.247
0.253
6
0.213
0,217
0.221
0.226
0.228
0.239
0.245
8
0.200
0.204
0.208
0.213
0,215
0.225
0.231
10
0.189
0.193
0.197
0.201
0.204
0,214
0,220
12
0.185
0,190
0.194
0.198
0.200
0.210
0,216
630
CHAPTER 36 — INSULATION OF PIPING
25 F; the thickness of insulation for brine is approximately 2J^ in. where
the temperature ranges from 0 deg to 25 F; and the thickness of insulation
where the brine temperature ranges from —30 F to zero degrees is ap-
proximately 4 in.
Insulation To Prevent Freezing
If the surrounding air temperature remains sufficiently low for an
ample period of time, insulation cannot prevent the freezing of still water,
or of water flowing at such a velocity that the quantity of heat carried in
the water is not sufficient to take care of the heat losses which will result
and cause the temperature of the water to be lowered to the freezing
point. Insulation can materially prolong the time required for the water
to give up its heat, and if the velocity of the water flowing in the pipe is
maintained at a sufficiently high rate, freezing may be prevented.
^ Table 11 may be used for making estimates of the thickness of insula-
tion necessary to take care of still water in pipes at various water and
surrounding air temperature conditions. Because of the damage and
service interruptions which may result from frozen water in pipes, it is
essential that the most efficient insulation be utilized. This table is
based on the use of hair felt or cork, having a conductivity of 0.30. The
initial water temperature is assumed to be 10 deg above, and the sur-
rounding air temperature 50 deg below the freezing point of water (tem-
perature difference, 60 F).
The last column of Table 11 gives the minimum quantity of water at
initial temperature of 42 F which should be supplied every hour for each
linear foot of pipe, in order to prevent the temperature of the water from
being lowered to the freezing point. The weights given in this column
should be multiplied by the total length of the exposed pipe line expressed
in feet. As an additional factor of safety, and in order to provide against
temporary reductions in flow occasioned by reduced pressure, it is
advisable to double the rates of flow listed in the table. It must be
emphasized that the flow rates and periods of time designated apply only
for the conditions stated. To estimate for other service conditions the
following method of procedure may be used.
If water enters the pipe at 52 F instead of 42 F, the time required to
cool it to the freezing point will be prolonged to twice that given in the
table, or the rate of flow of water may be reduced so that the quantity
required will be one-half that shown in the last column of Table 11.
However, if the water enters the pipe at 34 F it will be cooled to 32 F in
one-fifth of the time given in the table. It will then be necessary to in-
crease the rate of flow so that five times the specified quantity of water
will have to be supplied in order to prevent freezing.
If the minimum air temperature is — 38 F (temperature difference,
80 F), instead of —18 F, the time required to cool the water to the
freezing point will be 60/80 of the time given in the table, or the necessary
quantity of water to be supplied will be 80/60 of that given.
In making calculations to arrive at the values given in Table 11, the loss
of heat stored in the insulation, the effect of a varying temperature dif-
ference due to the cooling of pipe and water, and the resistance of the
outer surface of the insulation to the transfer of heat to the air have all
681
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TABLE 11.
DATA FOR ESTIMATING REQUIREMENTS TO PREVENT
FREEZING OF WATER IN PIPES
NOMINAL
NUMBER OF HOURS
WATER REQUIRED TO FLOW
PIPE
TO COOL
TO PREVENT FREEZING,
SIZE
WATER TO
POUNDS PER LINEAR FOOT OF
(INCHES)
FREEZING POINT
PIPE PER HOUR
Thickness of Insulation in Inches
1
2
3
1
2
3
1A
0.42
0.50
0.57
0.54
0.45
0.40
i
0.83
1.02
1.16
0.68
0.55
0.48
1H
1.40
1.74
2.02
0.84
0.68
0.58
2
1.94
2.48
2.90
0.95
0.75
0.64
3
3.25
4.27
5.08
1.24
0.94
0.79
4
4.55
6.02
7.20
1.47
1.11
0.93
5
5.92
7.96
9.69
1.73
1.29
1.06
6
7.35
9.88
12.20
1.98
1.46
1.19
8
10.05
13.90
17.25
2.46
1.78
1.44
10
13.00
18.10
22.70
2.96
2.12
1.70
12
15.80
22.20
28.10
3.43
2.46
1.93
been neglected. When these factors enter into the computations it is
necessary to enlarge the factor of safety. Also as stated, the time shown
in the table is that required to lower the water to the freezing point. A
longer period would be required to freeze the water, but the danger point
is reached when freezing starts. The flow of water will stop and the entire
line will be in danger as soon as the water freezes across the section of the
pipe at any point.
When water must remain stationary longer than the times designated in
Table 11, the only safe way to insure against freezing is to install a steam
or hot water line, or to place an electric resistance heater along the side of
the exposed water line. The heating system and the water line are then
insulated so that the heat losses from the heating system are not exces-
sive, and the heating effect is concentrated against the water pipe where
it is needed. For this form of protection 2 in. of an efficient insulation
may be applied.
Pipe Sweating
In some cases the prevention of condensation rather than the con-
servation of heat is the governing factor in determining the thickness of
insulation required. Fig. 2 may be used for determining the thickness of
any material of known conductivity which should be used to prevent con-
densation on pipes and flat metallic surfaces. The surface resistances used
for calculating the family of curves in Fig. 2 are based on the results of
tests made on canvas-covered pipe insulation surfaces at Mellon Institute.
However, it has been found that the resistance for asphaltic and roofing
surfaces is practically the same as for canvas surfaces, so that the curves
given may be followed with no alteration for surfaces commonly used.
Moisture will be deposited on a surface whenever its temperature falls
to that of the dew point, The maximum permissible temperature drop
is indicated on Fig. 2 at the point where the guide line passes through the
horizontal scale at the left center of the chart. This temperature drop
632
CHAPTER 36 — INSULATION OF PIPING
represents the difference between the dry-bulb temperature and the dew-
point temperature for the conditions involved. (See discussion of con-
densation in Chapter 7.)
The rate of heat loss from a surface maintained at constant temperature
is greatly increased by air circulation over the surface. In the case of
well-insulated surfaces the increases in losses due to air velocity are very
small as compared with increases shown for bare surfaces, because of the
\ \ ^ \ \
80 70 60 50 4-0 30 20
FIG. 2. THICKNESS OF PIPE INSULATION TO PREVENT SWEATING*
aSolve problems by drawing lines as indicated by dotted line, entering chart at lower left hand scale.
fact that air flowing over the surface of the insulation can increase only
the rate of heat transfer from surface to air, and cannot change the internal
resistance to heat flow inherent in the insulation itself. The maximum
increase in loss due to air velocity ranges from about 30 per cent in the
case of 1-in. thick insulation, to about 10 per cent in the case of 3-in. thick
insulation, provided that the insulation is thoroughly sealed so that air
can flow only over the surface.
633
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
ECONOMICAL THICKNESS OF INSULATION.
HOURS OPERATION PER YEAR
(L, B, McMillan, Bw. N&tional Dtit. Heating Axs'n*, Vol. 18, p, 131.)
FIG, 3. CHART FOR DETERMINING ECONOMICAL THICKNESS OF INSULATION
634
CHAPTER 36 — INSULATION OF PIPING
If the conditions are such that the air may circulate through cracks
and crevices in the insulation, the increases may be far greater than those
given. Therefore, it is essential that insulation be sealed as tightly
as possible. Pipe insulation out-of-doors should be provided with a
waterproof jacket, and other outdoor insulation should be thoroughly
weatherproof ed .
ECONOMICAL THICKNESS OF PIPE INSULATION
Table 12 shows the thicknesses of insulation which ordinarily are used
for various temperature conditions. Where a thorough analysis of
economic thickness is desired, this may be accomplished through the use
of the chart, Fig. 3.
The dotted line on the chart illustrates its use in solving a typical
example. In using the chart, start with the scale at the left bottom margin
representing the given number of hours of operation per year; then
proceed vertically to the line representing the given value of heat ; thence
horizontally, to the right, to the line representing the given temperature
difference; thence vertically to the line representing the conductivity of
TABLE 12. THICKNESSES OF INSULATION ORDINARILY USED lNDOORSa
THICKNESS OF INSULATION
STEAM PRESSURES
STEAM TEMPERATURES
(Le GAGE)
DEGREES
OR CONDITIONS
FAHRENHEIT
Pipes Larger
nrhnn i Tn
Pipes
2 In. to
Pipes
HIn.
4 In.
to 1H In.
Oto25
212 to 267
lin.
lin.
lin.
25 to 100
267 to 338
l^in.
1 in.
1 in.
100 to 200
338 to 388
2 in.
IJ^in.
lin.
Low Superheat
388 to 500
2^ in.
2 in.
1^2 in.
Medium Superheat
500 to 600
3 in.
2% in.
2 in.
High Superheat
600 to 700
3^ in.
3 in.
2 in.
aAU piping located outdoors or exposed to weather is ordinarily insulated to a thickness M in. greater
than shown in this table, and covered with a waterproof jacket.
the given material ; thence horizontally, to the left, to the line representing
the given discount on that material; thence vertically to the curve
representing the required per cent return on the investment; thence
horizontally, to the right, to the curve representing the given pipe size;
thence vertically to the scale at the top right margin where the economical
thickness may be read off directly. The dotted line on the chart illustrates
its use in solving a typical example.
Underground Insulation
Underground steam distribution lines are carried in protective struc-
tures of various types, sizes and shapes. (See Chapter 37.) Detailed
data on commonly used forms of tunnels and conduit systems have been
published by the National District Heating Association*.
Pipes in tunnels are covered with sectional insulation to provide
maximum thermal efficiency and are also finished with good mechanical
^Handbook ctf the National District Seating Association, Second Edition, 1932.
635
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
protection in the form of metal or waterproofing membrane outer
jackets. Conduit systems are in more general use than tunnels. Pipes
carried in conduits may be insulated with sectional insulation; however,
the more usual practice is to fill the entire section of the conduit around
the pipes with high quality, loose insulating material. The insulation
must be kept dry at all times, and for this purpose effective waterproofing
membranes enclose the insulation. A drainage system is also provided
to divert water which may tend to enter the conduit.
The economical thickness of insulation for underground work is dif-
ficult of accurate determination due to the many variables which have to
be considered. As a result of theories developed by J. R. Allen3, together
with experimental data presented by others, the usual endeavor is to
secure not less than 90 per cent efficiency for underground piping. Table
13 can be used as a guide in arriving at the minimum thickness of loose
insulation fills to use for laying out conduit systems. Other factors such
as the number of pipes and their combination of sizes, as well as the
standard conduit sizes, are primary controlling factors in the amount and
thickness of insulation for use.
When sectional insulation is applied to lines in tunnels or conduits,
usual practice is to apply the most efficient materials J^ in. less in thick-
ness than that determined by the use of Fig. 3. Fig. 3 is based on con-
ditions of insulation exposed to the air, whereas normal ground tempera-
ture is substituted for air temperature in determining the temperature
difference for use with the chart when applying it for underground pipe
line estimates.
TABLE 13. THICKNESS OF LOOSE INSULATION FOR USE AS
FILL IN UNDERGROUND CONDUIT SYSTEMS
MINIMUM THICKNESS OF INSULATION IN INCHES
MINIMUM
STEAM
STEAM
DISTANCE
PRESSURES
(La GAGE)
TEMPERATURES
DEGREES
STEAM LINES
RETURN LINES
BETWEEN
STEAM
OR CONDITIONS
FAHRENHEIT
Pipes Less
than 4 In.
Pipes 4 In.
to 10 In.
Pipes Larger
than 12 In.
Pipes Less
than 4 In.
Pipes 4 In.
and Larger
AND
RETURN
Hot Water,
or 0 to 25
212 to 267
1 3/i-j
2
2j/]2
1M
1J"12
1
25 to 125
267 to 352
2
2M
3
!}<£
1M
iM
Above 125, or
superheat
352 to 500
W*
3
m
1M
VA
m
•Theory of Heat Losses from Pipes Buried in the Ground, by J, R, Allen (A.S.H.V.E. TRANSACTIONS.
Vol. 26, 1920).
PROBLEMS IN PRACTICE
1 • Compute the total annual heat loss from 165 ft of 2-in. bare pipe in service
4000 hours per year. The pipe is carrying steam at 10 lb pressure and is exposed
to an average air temperature of 70 F.
The pipe temperature is taken as the steam temperature, which is 239.4 F, obtained
from Table 7, Chapter 1. The temperature difference between the pipe and air «= 239.4
— 70 « 169.4 deg. By interpolation of Table 1 between temperature differences of
157.1 F and 227.7 F, the heat loss from a 2-in. pipe at a temperature difference of 169.4
636
CHAPTER 36 — INSULATION OF PIPING
deg is found to be 1.677 Btu per hour per linear foot per degree temperature difference.
The total annual heat loss from the entire = 1.677 X 169.4 X 165 (linear feet) X 4000
(hours) = 188,000,000 Btu.
2 • Coal costing $11.50 per ton and having a calorific value of 13,000 Btu per
pound is being burned in the furnace supplying steam to the pipe line given in
Question 1. If the system is operating at an over-all efficiency of 55 per cent
determine the monetary value of the annual heat loss from the line.
The cost of heat per 1 million Btu supplied to the system = 1,000,000 X 11.5 (dollars)
-T- 13,000 (Btu) X 2000 (Ib) X 0.55 (efficiency) = $0.804. The total cost of heat
lost per year = 0.804 X 188 (million Btu) = $151. 15.4
3 • If the steam line given in Question 1 is covered with 1-in. thick 85 per cent
magnesia, determine the resulting total annual heat loss through the insula-
tion. Also compute the monetary value of the annual saving and the per-
centage of saving over the heat loss from the bare pipe.
By interpolation of Table 5 between temperature differences of 157.1 F and 227.7 F, the
coefficient of transmission for 1-in. magnesia on a 2-in. pipe is found to be 0.525 Btu per
hour per square foot of pipe surface per degree temperature difference at a temperature
difference of 169.4 deg. The total hourly loss per square foot of insulated pipe will then
be 0.525 X 169.4 « 89.04 Btu. From Table 2 the area per linear foot of 2-in. pipe is
found to be 0.622 sq ft. The total annual loss through the insulation = 89.04 X 0.622
X 165 (linear feet) X 4000 (hours) = 36,550,000 Btu. The annual bare pipe loss as
determined in the solution of Question 1 was found to be 188,000,000 Btu. The saving
due to insulation is then 188,000,000 — 36,550,000 = 151,350,000 Btu per year.
From the solution of Question 2 it was found that the heat supplied to the system cost
$0.804 per million Btu ; therefore, the monetary value of the saving = 0.804 (dollars)
X 151.35 (million Btu) = $121.69, or 81.2 per cent of the cost when using uninsulated
pipe.
4 • The manufacturer's list price for 85 per cent magnesia insulation is $0.36
per linear foot for 1-in. (standard thick) material to cover a 2-in. pipe. De-
termine the period of time required for the saving found in Question 3 to pay
for the cost of the insulation if it can be purchased and applied at 80 per cent
of list price (20 per cent discount).
The applied cost of insulation = 165 (linear feet) X 0.36 (dollars) X 0.80 (net)
— 47.52. Since the annual saving as found in Question 3 amounts to $121.69, the in-
sulation will pay for its cost in 47.52 -f- 121.69 — 0,3905 years; in other words, the cost
will be repaid 2.56 times by the saving obtained in one heating season.
5 • The conductivity of magnesia insulation is 0.455 at the mean temperature
which will result under the conditions of Question 3. Estimate the most
economical thickness of magnesia for application on the pipe when operating
under the conditions which are given in the foregoing problems and when a
20 per cent return is required on the investment for insulation.
Use chart given in Fig. 3. Begin at the left bottom margin and proceed successively as
shown by the dotted line example to the following essential data which are collected from
the problems previously given;
4000 hours operation per year,
$0.804 value of heat, dollars per million Btu.
169.4 deg temperature difference.
0.455 conductivity of insulation,
20 per cent discount from list, cost of insulation,
20 per cent fixed charges, return on investment.
2-in. pipe size.
Solution of the problem by use of Fig. 3 results in a required thickness of approximately
4 A closely approximate solution of this problem may be quickly made by use of the estimating chart given
In Fig, 1.
637
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
1.05 in. The nearest commercial thickness procurable is standard thick (1^2 in.)
magnesia.
(It is of interest to note that the use of Fig. 3 will generally result in solutions which, for all practical pur-
poses, agree closely with the specifications for thicknesses given in Table 12.)
6 • Determine the minimum thickness of wool felt insulation having a con-
ductivity of 0.30 necessary to prevent condensation of moisture on a 4-in. pipe
carrying cold water at a temperature of 40 F when the surrounding air reaches
maximum conditions of 90 F with a relative humidity of 90 per cent.
The difference between the temperature of the pipe and the surrounding air is 90 — 40
= 50 deg. For quick estimating purposes use the chart given in Fig. 2. Enter this chart
at the lower left margin on the 90 per cent relative humidity line and proceed horizontally
to the right to intersect the 90 deg air temperature line. Project a line up to the 50 deg
temperature difference line, and then horizontally to the right to the intersection with the
4-in. pipe size line. From this point proceed down to intersect the 0.30 line which denotes
the conductivity of the insulation. Directly opposite this point of intersection the correct
thickness of insulation is read from the scale on the lower right margin. This chart
solution denotes that wool felt 2.4-in. thick is sufficient to prevent condensation. The
nearest commercial thickness procurable is 2J^ in.
For prevention of condensation as well as for protection against freezing, if the thickness
determined theoretically cannot be had, it is better to apply the next greater thickness
procurable rather than to use any lesser thickness because an additional factor of safety
is thus obtained.
7 • A 3-in. pipe covered with 2 in. of hair felt insulation carries water out-of-
doors. Weather Bureau records for the locality denote that a minimum, out-
door temperature of zero F may be expected to prevail for a period not to exceed
10 hours. By use of Table 11 determine what degree of protection is provided
against freezing if the water is stationary in the line for the 10 hour period.
Table 11 denotes that 4.27 hours are required to lower water temperature from 42 F to
the freezing point (a 10 F drop) when the initial temperature difference between the
water and air is 60 F. The temperature drop in the example is 45 — 32 - 13 F and the
temperature difference is 45 — 0 -45 F. The time required to lower the water from
45 F to the freezing point will therefore be 4.27 X 1Ko X 6Ms = 7.4 hours.
It is evident that insufficient protection is provided to prevent freezing if a temperature
of zero F prevails outside for any period longer than 7 hours 24 min.
8 • With data given in Question 7 and its solution, determine the minimum
flow of water which must be maintained to prevent freezing if the length of
the water line is 85 ft.
From Table 11 it is seen that a flow of 0.94 Ib of water per linear foot per hour is suf-
ficient to prevent a drop in the water temperature from 42 F to the freezing point when
the temperature difference between air and water is 60 F. With the conditions stated, a
flow of 0.94 X 1%3 X 4%o » 0.542 Ib of water per linear foot of pipe line per hour, or
85 X 0.642 « 46.07 Ib of water per hour must flow through the line in order to prevent
freezing.
638
Chapter 37
DISTRICT HEATING
Underground Steam Piping, Selection of Pipe Sizes, Provision for
Expansion9 Capacity of Returns with Various Grades, Pipe Con-
duits, Pipe Tunnels, Service Connections, Steam per Square Foot
of Heating Surface, Fluid Meters and Metering, Rates
THOSE phases of district heating which frequently fall within the
province of the heating engineer are outlined here with data and
information for solving incidental problems in connection with institutions
and factories and for the design of heating systems for buildings which are
to be supplied with purchased steam. A complete district heating instal-
lation should not be attempted without a thorough study of the entire
problem by men competent and experienced in that industry.
UNDERGROUND STEAM PIPING
The methods used in district heating work for the distribution of steam
are applicable to any problem involving the supply of steam to a group of
buildings. The first step is to establish the route of the pipes, and in this
matter the local conditions so fully control the layout that little can be
said regarding it.
Having established the route of the pipes, the next step is to calculate
the pipe sizes. In district heating work it is common practice to design
the piping system on the basis of pressure drop. The initial pressure and
the minimum permissible terminal pressure are specified and the pipe
sizes are so chosen that the required amount of steam, with suitable
allowances for future increases, will be transmitted without exceeding
this pressure drop. The steam velocity is therefore almost disregarded
and may reach a very high figure. Velocities of 35,000 fpm are not con-
sidered high. By the use of this method the pipe sizes are kept to a
minimum with consequent savings in investment.
The steam flowing through any section of the piping can be computed
from a study of the requirements of the several buildings served. In
general a condensation rate of 0.25 Ib per hour per square foot of equiva-
lent heating surface is a safe figure. This allows for line condensation
which, however, is a small part of the total at times of maximum load.
Any unusual requirements such as those for process steam should be
individually calculated.
The steam requirements for water heating should be taken into account,
but in most types of buildings this load will be relatively small compared
with the heating load and will seldom occur at the time of the heating
639
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
peak. Unusual features such as large heaters for swimming pools should
not be overlooked.
The pressure at which the steam is to be distributed will depend, in
part, upon whether or not it has been passed through electrical generating
units. If it has, the pressure will be considerably lower than if live steam,
•direct from the boilers, is used. The advantages of low pressure distribu-
tion (2 to 30 Ib per square inch) are (1) smaller heat loss from the pipes,
(2) less trouble with traps and valves, and (3) simpler problems in pressure
reduction at the buildings. With distribution pressures not exceeding
40 Ib per square inch there is little danger even if the full distribution
pressure should build up in the radiators through the faulty operation of
a reducing valve; but with pressures higher than this a second reducing
valve or some form of emergency relief is usually desirable to prevent
excessive pressures in the radiators. The advantages of high pressure
distribution are (1) smaller pipe sizes and (2) greater adaptability of the
steam to various operations other than building heating.
The different kinds of apparatus which frequently must be served
require various minimum pressures. Kitchen equipment requires from
5 to 15 Ib per square inch, the higher pressures being necessary for
apparatus in which water is boiled, such as stock kettles and coffee urns.
An increased amount of heating surface, which is easily obtained in some
kinds of apparatus, results in quicker and more satisfactory operation at
low pressures. For laundry equipment, particularly the mangle, a pres-
sure of 75 Ib per square inch is usually demanded although 30 Ib per square
inch is sufficient if the mangle is equipped with a large number of rolls and
if a slow rate of operation is permissible. Pressing machines and hospital
-sterilizers require about 50 Ib per square inch.
PIPE SIZES
The lengths of pipe, steam quantities, and initial and terminal pressures
having been chosen, the pipe sizes can readily be calculated by means of
the Unwin pressure drop formula. This formula, which gives pressure
-drops slightly larger than actual test results, is as follows:
0.0001306 W*L (* + ~f )
(1)
where
P =» pressure drop, pounds per square inch.
W = weight of steam flowing, pounds per minute.
L «s length of pipe, feet.
d as inside diameter of pipe, inches.
y as average density of steam, pounds per cubic foot.
This formula is similar to the Babcock formula given in Chapter 32.
Information on provision for expansion will be found in Chapters
32 and 34.
In general, return lines when installed follow the contour of the land,
and Table 1 gives sizes of return pipes for various grades. It is evident
that at points where the grade is great, smaller pipes can be installed.
640
CHAPTER 37 — DISTRICT HEATING
PIPE CONDUITS
Conduits for steam pipes buried underground should be reasonably
waterproof, able to withstand earth loads and to take care of the expan-
sion and contraction of the piping without strain or stress on the couplings,
or without affecting the insulation or conduit. Expansion of the piping
must be carefully controlled by means of anchors and expansion joints
or bends so that the pipes can never come in contact with the conduit.
Anchors can be anchor fittings or U-shaped steel straps which partially
encircle the pipes and are firmly bolted to a short length of structural
steel set in concrete.
TABLE 1.
CAPACITY OF RETURNS FOR UNDERGROUND DISTRIBUTION SYSTEMS IN
POUNDS OF CONDENSATE PER HOUR
SlZEa
PITCH OF PIPE PER 100 FT.
OF PIPE
IN.
6"
i'
2'
3'
5'
10'
20'
1
448
998
1890
2240
3490
5490
7490
1M
1740
2490
3990
4880
6480
9480
13500
1J4
2700
4190
5740
7480
9480
14500
20900
2
4980
7380
10700
13900
16900
24900
36900
3
13900
22500
30900
37400
50400
74800
105000
4
30900
44800
64800
79700
105000
154000
229000
5
54800
79800
120000
144800
195000
294000
418000
6
90000
138000
187000
237000
312000
449000
8
190000
277000
404000
508000
660000
938000
10
344000
498000
724000
900000
1190000
12
555000
798000
1148000
1499000
1990000
•Size of pipe should be increased if it carries any steam.
In laying out conduits of this type the following points should be
borne in mind:
1. An expansion joint offset or bend should be placed between each two anchors.
2. If the distance between buildings is 150 ft or less and the steam line contains high-
pressure steam, the line may be anchored in the basement of one building and allowed to
expand into the basement of the second building. If the steam line contains low-pressure
steam (up to 4-lb pressure), this method may be used if buildings are 250 ft or less apart.
3. If the distance between buildings is between 150 ft and 300 ft and the steam line
contains high-pressure steam, the lines should be anchored midway between the buildings
and allowed to expand into the basements of both buildings. If the steam line contains
low-pressure steam this method may be used if buildings are between 250 ft and 600 ft
apart. No manhole is required at the anchor, and a blind pit is all that is necessary,
4. For longer lines, manholes must be located according to judgment and depending
upon the expansion value of the type of expansion joint or bend that is used. The
minimum number of manholes will be required when an expansion bend or an anchor
with double expansion joint is placed in each manhole and the pipes are anchored mid-
way between manholes.
5. A proper hydrostatic test should be made on the assembled line before the insula-
tion and, the top of the conduit are applied. The hydrostatic pressure should be one-
and-one-half times the maximum allowable pressure and it should be held for a period of
at least two hours without evidence of leakage. In any case the pressure should be no-
less than 100 Ib per square inch.
The styles and construction of conduits commonly used may be classi-
fied as follows. Some of the more common forms are illustrated in Fig. 1.
Wood Casing: The pipe is enclosed in a cylindrical casing usually having a wall 4 in.
thick and built of segments which are bound together by a wire wrapped spirally around
641
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
the casing. The casing is lined with bright tin and coated with asphaltum. The pipe is
supported on rollers carried in a bracket which fits into the casing. The lengths of
casing are tightly fitted together with a male and female joint. This form of conduit is
illustrated in Fig. 1 at A . The casing rests on a bed of crushed stone with tile drains laid
below. The tile drains are of 4-in. field tile or vitrified sewer tile, laid with open joints.
Filler Type: The pipes are supported on expansion rollers properly supported from
the conduit or independent masonry base. The pipes are protected by a split-tile conduit,
and the entire space between the pipes and the tile is filled with an insulating filler. Thus
the pipes are nested and the insulation between them and the tile effectively prevents
circulation of air. The conduit is placed on a bed of gravel or crushed rock from 4 to 6 in.
thick, which is extended upward so as to come about 2 in. above the parting lines of the
tile. A tile underdrain is placed beneath the conduit throughout the entire length and is
connected to sewers or to some other point of free discharge. At B and D in Fig. 1 are
shown two forms of tile conduit of the filler type.
Circular Tile or Cast-Iron Conduit: The pipes are carried on expansion rollers sup-
ported on a frame which rests entirely on the side shoulders of the base drain foundation.
FIG, 1. CONSTRUCTION DETAILS OF CONDUITS COMMONLY USED
A he pipes are protected by a sectional tile conduit, scored for splitting, or a cast-iron
conduit, both being of the bell and spigot type. The conduit has a longitudinal side joint
for cementing, after the upper half of conduit is in place, so shaped that the cement is
keyed in place while locking the top and bottom half of the conduit together with a
water-tight vertical side joint. The cast-iron conduit has special side locking clamps in
addition to the vertical side joint. The entire space between the conduit and the pipes is
filled with a water-proofed asbestos insulation. The conduit is supported on the base
drain foundation, each section resting on two sections of the base drain, thus inter-
locking, The base drain is so shaped that it provides a cradle for the conduit* resting
solidly on the trench bottom and providing adequate drainage area immediately under the
conduit. The underdrain is connected to sewers or some other point of free discharge.
For tile conduit the base drain is vitrified salt glazed tile and for cast-iron conduit it is
either extra heavy tile or cast-iron. A free internal drainage area is also provided to carry
away any water that may collect on the inside of the conduit from a leaky pipe or joint in
the conduit. Broken stone is filled in around the base drain and up to the vertical side
joint. The broken stone is covered with an asphalted filter cloth to prevent sand
from sifting through the broken stone and clogging the drainage area of the base drain.
The tile conduit is made in 2- ft lengths and the cast-iron conduit in 4-ft lengths, cast in
642
CHAPTER 37 — DISTRICT HEATING
separate top and bottom halves. Special reinforcing ribs give the cast-iron conduit ample
strength with minimum weight.
Insulated Tile Type: The insulating material, diatomaceous earth, is molded to the
inside of the sectional tile conduit. The space between the pipes and the insulating con-
duit lining may also be filled with insulation. The pipes are carried on expansion rollers
supported on a frame which rests on the side shoulders of the base drain foundation.
This type of conduit has the same mechanical features as those described under the
heading Circular Tile or Cast-Iron Conduit.
Sectional Insulation Type (Tile or Cast-iron): Each pipe is insulated in the usual way
with any desired type of sectional pipe insulation over which is placed a standard water-
proof jacket with cemented joints. The pipes are enclosed in a sectional tile or cast-iron
conduit as described under the heading Circular Tile or Cast-Iron Conduits.
Sectional Insulation Type (Tile or Concrete Trench) : A type of construction frequently
used in city streets, where service connections are required at frequent intervals, the
pipes are insulated as described in the preceding paragraph, and are enclosed^ in a box
or trench made either entirely of concrete, or with concrete bottom and specially con-
structed tile sides and tops. The pipes are supported on roller frames secured in the
concrete. At C and E, Fig. 1, are shown two tile conduits using sectional insulation. In
these particular designs the space surrounding the pipe is filled partially or wholly with a
loose insulating material. The use of loose material in addition to the sectional insula-
tion is, of course, optional and is only justifiable where high pressure steam is used. The
conduit shown at F is of a similar type and has the advantage of being made entirely of
concrete and other common materials.
Sectional Insulation Type (Bituminized Fibre Conduit) : Each pipe is individually
insulated and encased in a bituminized fibre conduit. The insulating material is 85
per cent carbonate of magnesia sectional pipe covering, applied in the usual manner as
on overhead pipes, except that bands are omitted. After every fifth section of magnesia
covering there is applied a short, hollow section of very hard asbestos material in the
bottom portion of which rests a grooved-iron plate carrying ball-bearings ^ upon which
the pipe rides when expanding or contracting. This short expansion section is of the
same outside diameter as the adjacent 85 per cent magnesia covering. Over the pipe
covering and expansion device there are placed two layers of bituminized ( fibre conduit
with all joints staggered, and the surface of each conduit is finished with liquid cement.
Conduits are placed on a bed of crushed rock or gravel, approximately 6 in. deep, and
this is extended upward to about the center line of the conduit when trench is backfilled.
Underdrains leading to points of free discharge are placed in the gravel or crushed
rock beds.
Special Water-Tight Designs: It is occasionally necessary to install pipes in a very wet
ground, which calls for special construction. The ordinary tile or concrete conduit is not
absolutely water tight even when laid with the utmost care. The conduit shown at G,
Fig, 1, is of cast-iron with lead-calked joints and is water tight if properly laid. It is
obviously expensive and is justified only in exceptional cases. A reasonably satisfactory
construction in wet ground is the concrete or tile conduit with a waterproof jacket
enclosing the pipe and its insulation, and with the interior of the conduit carefully
drained to a manhole or sump having an automatic pump. It is useless to install external
drain tile when the conduit is actually submerged. •
PIPE TUNNELS
Where steam heating lines are installed in tunnels large enough to
provide walking space, the pipes are supported by means of hangers or
roller frames on brackets or frame racks at the side or sides of the tunnel.
The pipes are insulated with sectional pipe insulation over which is
placed a sewed-on, painted canvas jacket or a jacket of asphalt-saturated
asbestos water-proofing felt. The tunnel itself is usually built of concrete
or brick and water-proofed on the outside with membrane water-proofing.
On account of their relatively high first cost as compared with smaller
conduits, walking tunnels are sometimes not installed where provision for
the heating lines is the only consideration, but only where they are required
643
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
to accommodate miscellaneous other services or provide underground
passage between buildings.
SERVICE CONNECTIONS
Most district heating companies enforce certain regulations regarding
the consumer's installation, partly to safeguard their own interests but
principally to insure satisfactory and economical service to the consumer.
Heating mam
Unions
Pipe to connect into steam mam not less
than 10 feet from reducing valve, i( possible
FIG. 2. CONNECTIONS FOR REDUCING VALVES OF SIZE LESS THAN 4 INCHES
There are certain fundamental principles that should be followed in the
design of a building heating system which is to be supplied from street
mains. Although some of these apply to any building, they have been
demonstrated to be especially important when steam is purchased.
Bypass valve'
Heating mam
Service valve
Balance pipe
Pipe to connect into steam mam not less
than 10 feet from reducing valve, if possible
FIG. 3. CONNECTIONS FOR REDUCING VALVES OF SIZE 4 INCHES AND
LARGER, AND FOR EXPANDED VALVES
Figs. 2 and 3 show typical service connections used for low pressure
steam service. As shown in Fig. 2, no by-pass is used around the reducing
valve on sizes less than 4 in* Fig. 3 illustrates the use of a by-pass around
reducing valves 4 in. and larger. This latter . construction permits the
644
CHAPTER 37 — DISTRICT HEATING
operation of the line in case of failure in the reducing valve. In the smaller
sizes, the reducing valve can be removed, a filler installed, and the house
valve used to throttle the flow of steam.
Fig. 4 shows a typical installation used for high pressure steam service.
The first reducing valve, usually furnished by the utility company,
Pressure reducing valve
At least 12 feet of pipe
Customer's work
starts here
Note.- All valves, fittings, and traps up to
and including customer's control
valve to be at least equal to
American Standard 175 Ib S. S P.
Pipe to be standard weight
Continuous-flow type
float trap
FIG. 4. STEAM SUPPLY CONNECTION WHEN USING CONDENSATION METER
effects the initial pressure reduction. The second reducing valve, usually
furnished by the customer, reduces the steam pressure to that required.
1 . Provision should be made for conveniently shutting off the steam supply
at night and at other times when heat is not needed.
It has been thoroughly demonstrated that a considerable amount of
heat can be saved by shutting off steam at night. Although there is, in
Return main
Condensation meter
and manifold castmi
Vent
[V- Preheated water
to heater
- -Carry full size to sewer
• — Gas seal
FIG. 5. RETURN PIPING FOR CONDENSATION METER
some cases, an increased consumption of heat when steam is again turned
on in the morning, there is a large net saving which may be explained by
the fact that the lower inside temperature maintained during the night
obviously results in lower heat loss from the building, and less heat need
therefore be supplied.
Steam can be entirely shut off at night in most buildings even in very
645
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
CHAPTER 37 — DISTRICT HEATING
cold weather without endangering plumbing. It is necessary, however, to
have an ample amount of heating surface so that the building can be
quickly warmed in the morning. Where the hours of occupancy differ in
various parts of the building, it is good practice to install separate supply
pipes to the different parts. For example, in an office building with
stores or restaurants on the first floor which are open in the evening, a
separate main supplying the first floor will permit the steam to be shut off
from the remainder of the building in the late afternoon. The division of
the building into zones each with a separately controlled heat supply is
sometimes desirable, as it permits the heat to be adjusted according to
variations in sunshine and wind.
#. Residual heat in the condensate should be salvaged.
This heat may be salvaged by means of a cooling radiator, or as is more
frequently done, by a water heating economizer (see Fig. 5) which pre-
heats the hot water supply to the building. Fig. 6 shows a typical steam
service installation for high pressure steam, complete for steam flow
metering, water heating, preheating, automatic heating control, and for
using steam for other purposes.
The condensation from the heating system, after leaving the trap,
passes through the preheater on its way to the meter. The supply to the
hot water heater passes through the preheater, absorbing heat from the
condensation. If the hot water system in the building is of the recircu-
lating type, the recirculating connection should be tied in between the
preheater and the water heater proper, not at the preheater inlet, because
the recirculated hot water is itself at a high temperature. The number of
square feet of heating surface in the preheater should be approximately
equal to one per cent of the equivalent square feet of heating surface in the
building.
Because of the lack of coincidence between the heating system load and
the hot water demand, a greater amount of heat can be extracted from the
condensation if storage capacity is provided for the preheated water.
Frequently a type of preheater is used in which the coils are submerged
in a storage tank.
8. Heat supply should be graduated according to variations in the outside
temperature.
This may be done in several ways, as by the use of thermostats of
various types or by orifice systems. Another method which is very simple
is the use of an ordinary vacuum return line system in which the pressure
in the radiators is varied between a high vacuum and a few pounds pres-
sure, thus producing some control over the heat output. One form of con-
trol which appears to be well suited for controlling district steam service
to a building is the weather compensating thermostat. It regulates the
steam supply automatically according to the outdoor temperature, and
gives frequent short intervals of intermittent steam supply, and at the
same time insures delivery of steam to all the radiators.
Another form of regulation, known as the time-limit control, is sometimes
employed for regulating the steam supply from the central station main to
the building. Such a control provides an intermittent supply of steam to
the radiation either throughout the 24 hours of the day or during the day-
647
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
time hours only. The setting of a switch may provide no service, con-
tinuous service, or periodic service. For the latter, by means of several
intermittent settings, steam will be supplied during each period in in-
crements of a certain number of minutes for each successive setting of the
switch, steam being shut off during the balance of the period. These
settings afford from 15 to 80 per cent of the maximum heating effect
required on days of zero temperature. A night switch with a variety of
settings may be adjusted so as to maintain throughout the night the
intermittent supply called for by the day switch setting, or may be set to
interrupt the operation of the day switch and entirely cut off the supply
of steam to the radiation at night during certain hours which are selected
by the operating engineer.
FLUID METERS
No one thing has contributed more to the advancement of district
heating than the perfection of fluid meters, which may be classified as
follows :
1. Positive Meters: The fluid passes in successive isolated quantities — either weights
or volumes. These quantities are separated from the stream and isolated by alternately
filling and emptying containers of known capacity.
2. Differential Meters: The fluid does not pass in isolated separately-counted quan-
tities but in a continuous stream which may flow through the line without actuating
the primary device of the meter. In the differential meter, the quantity of flow is not
determined by simple counting, as with the positive meter, but is determined from the
action of the steam on the primary element.
Additional subdivisions of these two general classifications can be made
as follows :
Fluid
Meters
Positive - quantity
Weighing
Volumetric
f Weighers
\ Tilting trap
/ Rotary
\ Bellows
Quantity - Current - Turbine
Ferential <
Rate of
flow
Head
(Kinetic)
Area
(Geometric)
IVenturi
Flow nozzle
Orifice
Pitot tube
( Orifice and plug
\ Cylinder and piston
Head area
(Weir)
f V-notch
\ Special notch
In selecting a meter for a particular installation, the number of different
makes and types of meters suitable for the job is usually limited by
one or more of the following considerations:
1. Its use in a new or an old installation.
2. Method to be used in charging for the service.
3. Location of the meter.
4. Large or small quantity to be measured.
5. Temporary or permanent installation.
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CHAPTER 37 — DISTRICT HEATING
Pressure reducing valve
and zap
Vents and loops unnecessary
where meter is 5 feet or
more below pipe
Note.- All valves, fittings, and traps up to
and including customer's control
valve to be at least equal to
American Standard 175 Ib S. S, P
Pipe to be standard weight
FIG. 7. ORIFICE METER STEAM SUPPLY CONNECTION
6. Cleanliness of the fluid to be measured.
7. Temperature of the fluid to be measured.
8. Accuracy expected.
9. Nature of flow: turbulent, pulsating, or steady.
10. Cost.
(a) Purchase price.
(&) Installation cost.
(c) Calibration cost.
(d) Maintenance cost.
11. Servicing facilities of the manufacturer.
12. Pressure at which fluid is to be metered.
13. Type of record desired as to indicating, recording or totalizing.
14. Stocking of repair parts.
15. Use of open jets where steam is to be metered.
16. Metering to be done by one meter or by a combination of meters.
17. Use as a check meter.
18. Its facilities for determining or recording information other than flow.
Condensation Meters
The majority of the meters used by district heating companies in the
sale of steam to their customers are of the condensation or flow types.
The condensation meter is a popular type for use on small and medium
sized installations, wnere a^ °f tne condensate can be brought to a com-
mon point for metering purposes. Its simplicity of design, ease in testing,
accuracy at all loads, low cost, and adaptability to low pressure distri-
bution has made it standard equipment with many heating companies.
Two types of condensation meters are in general use : the tilting bucket
meter and the revolving drum or rotor meter of which there are several
makes on the market. Condensation meters should not be operated under
649
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
pressure; they are made for either gravity or vacuum installation. Con-
tinuous flow traps are necessary ahead of the meter if a vented receiver is
not used. Where bucket traps are used, a vented receiver before the
meter is essential. If desirable a receiver may be used with a continuous
flow trap, but this is not necessary.
Steam flow meters are available in many types and combinations, as
indicated in the subdivision covering fluid meters on page 648.
The orifice and plug meter is one in which the steam flow varies directly
as the area of the orifice. The vertical lift of the plug, which is proportional
to the flow, is transmitted by means of a lever to an indicator and to a
CONSTANT PLOW TRAP,
VENT
GRAVITY TYPE
CONDENSATION
METER-?
GRAVITY DISCHARGE
UJ
FIG. 8. GRAVITY INSTALLATION FOR CONDENSATION METER
USING VENTED RECEIVERS
pencil arm which records the flow on a strip chart. The total flow over a
given period is obtained by measuring the area by using a plani meter
on the chart and applying the meter constant.
Fig. 7 shows a typical orifice type meter connection and indicates
typical requirements in the installation of this type of meter. Fig. 8
illustrates a gravity installation using a vented receiver ahead of the
meter, while Fig. 9 shows a vacuum installation without a master trap.
Flow meters using an orifice, Venturi tube, flow nozzle, or Pi tot tube
as the primary device are made by a number of manufacturers and can
be obtained in either the mechanically or electrically operated type. The
electric flow meter makes it possible to locate the instruments at some
distance from the primary element*
Flow meters employing the orifice, Venturi tube, flow nozzle or Pitot
tube should be so selected as to keep the lower operating range of the
load above 20 per cent of the capacity of the meter. This is desirable for
accuracy as the differential pressure at light loads is too small to properly
actuate the meter. A few general points to be considered in installing a
meter of this type are:
1. It is desirable to place the differential medium in a horizontal pipe in preference
to a vertical one, where either location is available.
2, Reservoirs should always be on the same level and installed in accordance with the
instructions of the meter company.
660
CHAPTER 37 — DISTRICT HEATING
3. The meter body should be placed at a lower level than that of the pressure differ-
ential medium. Special instructions are furnished where the meter body is above.
4. Meter piping should be kept free from leaks.
5. Sludge should not be permitted to collect in the meter body.
6. The meter body and meter piping should be kept above freezing temperatures.
7. It is best not to connect a meter body to more than one service.
8. Special instructions are furnished for metering a turbulent or pulsating flow.
STEAM PER SQUARE FOOT OF HEATING SURFACE
The following factors are used in New York City for the different classes
of buildings listed. The factors are based on maintaining an inside tern-
VACUUM
LINE FROM
RADIATORS
BY-PASS
VACUUM TYPE
CONDENSATION
METER-
-TO VACUUM PUMP
FIG. 9. VACUUM CONDENSATION METER INSTALLATION WITHOUT MASTER TRAP
perature of 70 F for certain hours, with a minimum outside temperature of
0 F and an average of 43 F for the heating season of eight months (October
1 to June 1). In this group are six types of buildings:
Manufacturing or commercial loft type where steam is used to heat the premises during
the day hours to maintain 65 to 68 F from 9 a.m. to 5 p.m. No Sunday or holiday use
and no night use. Factor : 325 Ib per square foot of heating surface per season,
Office buildings using steam during daylight hours to maintain 70 F from 9 a.m. to
6 p.m. for approximately 240 days (heating season), No night use, Factor: 400 Ib per
square foot of heating surface per season.
Office buildings using steam during day hours and at night when required to 7, 8 and
9 p.m. (customary where there are stock brokers or banking offices), 240 days. Factor:
500 Ib per square foot of heating surface per season.
Residences of the block type (not detached) where high-class heatir*g service is re-
quired; somewhat similar to apartment buildings. . Factor: 550 Ib per square foot of
heating surface per season,
651
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Apartment houses where high-class heating service is required. (Steam off at mid-
night.) Factor: 650 Ib per square foot of heating surface per season.
Hotels (commercial type) where very high-class service is required for 24 hours.
Factor: 800 Ib per square foot of heating surface per season.
By assuming one square foot of equivalent heating surface for each
100 cu ft of space heated, which seems a fair ratio in New York City, it is
possible roughly to estimate the steam required per cubic foot of space,
information which is often more easily obtained than the square feet of
heating surface. Additional data on the heating requirements of various
types of buildings in a number of cities may be found in the Handbook
of the National District Heating Association.
RATES
Fundamentally, district heating rates are based upon the same princi-
ples as those recognized in the electric light and power industry, the main
object being a reasonable return on the investment. However, there are
other requirements to be met ; the rate for each class of service should be
based upon the cost to the utility company of the service supplied and
upon the value of the service to the consumer, and it must be between
these two limits. The profit need not be divided proportionately among
the rated groups, but should be established from a competitive stand-
point. District heating rates should be designed to produce a sufficient
return on the investment regardless of weather conditions, although
existing rate schedules do not conform with this principle. Lastly, the
rate schedule must be reasonably easy for the intelligent layman to
comprehend.
Depreciation should be based on a careful estimate of the life of various
elements of the property. Appropriations to reserves should be made,
with generosity in good years and with discretion in less favorable years.
Glossary of Terms
Load Factor. The ratio, in per cent, of the average load to the maxi-
mum load. This is usually based on a one year period but may be applied
to any specified period.
Demand Factor. The relation between the connected radiator surface
or required radiator surface and the demand of the particular installation,
It varies from 0.25 to 0.3 Ib per hour per square foot of surface.
Diversity Factor, The ratio of the sum of the individual demands of a
number of buildings to the actual composite demand of the group.
Types of Rates
A. Flat Rates.
1. Radiator surface charge. Obsolescent,
JB. Meter Rates.
1. Straight-line.
2. Step. Obsolescent.
3. Block.
(a) Class rates.
C. Demand Rates.
1. Flat demand,
2. Wright.
3. Hopkinsoru
4. Doherty (or Three charge).
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CHAPTER 37 — DISTRICT HEATING
Straight-Line Meter Rate. The price charged per unit is constant, and the consumer
pays in direct proportion to his consumption without regard to the difference in costs of
supplying the individual customers.
Block Meter Rate, The pounds of steam consumed by a customer are divided into
blocks of M pounds each, and lower rates are charged for each successive block consumed.
This type of charge predominates in steam heating rate schedules for it has the ad-
vantage of proportioning the bill according to the consumption and the cost of service.
It has the disadvantage of not discriminating between customers having a high load
factor (relatively low demand) and those haying a low load factor (relatively high
demand). The utility company must maintain sufficient capacity to serve the high
demand customers and the cost of the increased plant investment is divided equally
among the users, so the high demand customers are benefited at the expense of the
others.
Demand Rates. These refer to any method of charge based on a measured maximum
load during a specified period of time.
The flat demand rate is usually expressed in dollars per M Ib of demand per
month or per annum. It is based on the size of a customer's installation, and is
seldom used except where a flow meter is not practicable.
The Wright demand rate is similar in calculation to the block rate except that it is
expressed in terms of hours' use of the maximum demand. It is seldom used but
forms the basis for other forms of rates.
The Hopkinson demand rate is divided into two elements:
(a) A charge based upon the demand, either estimated or measured;
(&) A charge based upon the amount of steam consumed.
This rate may be modified by dividing the quantities of steam demanded and
consumed into blocks charged for at different rates.
Demand rates are comparatively new and are not yet widely used; though they are
equitable and competitive they are difficult for the average layman to understand.
They are of benefit to utility companies and to consumers because the investment and
operating costs can be divided to suit the particular circumstances into demand, cus-
tomer, and consumption groups through the use of some modification of the Hopkinson
rate,
Fuel Price Surcharge, It is usually desirable to establish a rate upon a specified basic
cost of fuel to the utility company. Where there are wide variations in the price of fuel,
it is also desirable to add a definite charge per M Ib of steam sold for each increment of
increase in the price of fuel. This surcharge automatically compensates for the variations
without necessitating frequent changing of the whole rate structure,
REFERENCES
Pipe Line Design for Central Station Healing, by B. T. Gifford (A.S.H.V.E, TRANSACTIONS, Vol. 17, 1911).
Engineering and Cost Data Relative to the Installation of Steam Distributing Systems in a Large City, by
F. H. Valentine (A.S.H.V.E, TRANSACTIONS, Vol. 22, 1916).
Transmission of Steam in a Central Heating System, by J. H. Walker (A.S.H.V.E. TRANSACTIONS,
Vol. 23, 1917).
Efficiency of Underground Conduit, by G. B. Nichols (A.S.H.V.E. TRANSACTIONS, Vol. 23, 1917).
Economical Utilization of Heat from Central Plants, by N, W. Calvert and J, E. Seiter (A.S.H.V.E.
TRANSACTIONS, Vol. 30, 1924).
Standard Connections for Condensation Meiers, (N.D.H.A. Proceedings, Vol. XII, pp. 63-76).
Installation and Maintenance of Steam Meters, (N.D.H.A. Proceedings, Vol. XIII, pp. 177-183),
Inaccuracy in Flow Meter Calculations, (N.D.B.A. Proceedings, Vol. XIII, pp. 183-193),
Testing of Steam Meters, (N.D.H.A. Proceedings, Vol. XIV, pp. 272-276).
Meter Accuracy Guarantees, (N.D.H.A. Proceedings Vol. XIV, pp. 276-277),
Effect of Pulsations on the Flow of Cases, (N.D.H.A, Proceedings, Vol. XIV, pp. 277-281).
Meter Connections, (N.D.H.A. Proceedings, Vol. XX, pp, 126-143).
Layout for Testing Meters, (N.D,H,A. Proceedings, Vol. XX, pp. 391-392),
Characteristic Meter Calibration Curves (N.D.ff.A- Proceedings, Vol. XX, pp. 444-453),
Rates (N.D.H.A. Handbook, 1932, Chapter 10).
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
PROBLEMS IN PRACTICE
1 • What is the common method of determining the size of mains in a dis-
tribution system?
On the basis of pressure drop: The initial pressure and the minimum permissible
terminal pressure are specified, and the pipe sizes are so chosen that the maximum
estimated amount of steam may be transmitted without exceeding this pressure dif-
ference. The steam's velocity is disregarded and it may reach a magnitude in excess of
35,000 fpm which is not considered high.
2 • a. What are the advantages and disadvantages of a low pressure distribu-
tion system?
b. High pressure?
a. The advantages of a low pressure distribution system include:
1. Smaller heat loss from the pipes.
2. Less trouble with traps and valves.
3. Simpler problems with pressure reducing equipment at the buildings.
4. No danger to building heating equipment from high pressure through failure of the
reducing valves.
The disadvantages of a low pressure system are:
1. Larger pipe sizes.
2, Decreased field of usefulness owing to small pressure range.
b. The advantages of a high pressure system are:
1. Smaller pipe sizes.
2, Greater adaptability of the steam to various uses other than building heating.
The disadvantages of a high pressure system are :
1. Large heat loss from the pipes.
2. The high pressure traps and valves required often give more trouble than low
pressure traps and valves do.
3. Extra heavy fittings are required.
4. Usually two reducing valves or some form of emergency relief is necessary to
protect the building piping system.
3 • Determine the size of pipe from the following data using Unwin's formula:
Length of pipe, 600 ft.
Steam to be carried, 90,000 Ib per hour, dry saturated.
Initial pressure, 100 Ib per square inch, gage.
Final pressure, 40 Ib per square inch, gage.
Using the formula:
0,0001306 W*L ( 1 4- ~>
p « _.^____i „£,
yd*
The pressure drop P » 100 — 40 » 60 Ib per square inch.
90 000
The weight of steam per minute W =* — ~— - ** 1500,
The length of pipe in feet L » 600.
The average density of steam y in pounds per cubic foot, taken fyrc-ni ^teenan's Tf^ble:
At 100-lb gage, y - 0.2578
At 40-lb gage, y » 0.1285
Average, y « 0.1932
The diameter of the pipe in inches =» d.
654
CHAPTER 37 — DISTRICT HEATING
Substituting the values in the formula:
0.0001306 X 15002 X 600 ( 1 + ^
fi0 _ V &
°U 0.1932 X #
d « 7.35 in.
Therefore, an 8-in. pipe should be used.
4 • What points should be borne in mind when laying out an underground
steam conduit?
The conduit should be reasonably waterproof, able to withstand earth loads and to take
care of the expansion and contraction of the piping without strain or stress on the
couplings, or without affecting the insulation or the conduit. Expansion of the piping
must be carefully controlled by means of anchors and expansion joints or bends so that
the pipes can never come in contact with the conduit.
5 • What is considered the proper pressure for a hydrostatic test before com-
pleting the conduit?
In the case of any underground piping which is to be ^buried or otherwise made inacces-
sible, the assembled lines shall first be tested hydrostatically at a pressure of one and one-
half times the maximum allowable service pressure and held for a period of at least two
hours without evidence of leakage. In any case the hydrostatic pressure should not be
less than 100 Ib per square inch.
6 • What factors should be considered before determining the route of a steam
line?
1. The line should be so located that it will bring in the greatest revenue (or supply the
most steam) with the least cost.
2. The ultimate length and size of services and branches necessary with each possible
location should be estimated, for mains should be run near to the big loads.
3. The location of the boiler room or piping center of present and future buildings to be
served should be considered.
4. Where possible, make the lines straight between manholes.
5. Avoid such obstructions as other lines, sewers, ducts, curb drains, manholes, valve
boxes, catch basins, fire hydrants, and poles; especially avoid electric ducts and water
lines.
6. Avoid locating lines near where pile driving and foundation construction for new
buildings will take place.
7. Consider construction difficulties such as traffic, hard rock, and wet earth, which
increase time and labor,
8. Consider the economies of using available sidewalk vaults of buildings. Weigh the
advantage of less excavation against the cost of obstruction removal,
9. Consider all operating difficulties,
10. Consider the difficulties of negotiating agreements for lines on private property
where public and private rights-of-way are available.
11. Consider the effect of proposed municipal and other improvements.
12. Consider municipal regulations.
7. • State the advantages and disadvantages of tunnels over conduits.
The advantages of pipe tunnels over conduits are:
1. Accommodation for miscellaneous services other than steam.
2. Provision of an underground passage between buildings.
3. Easy installation of additional pipes and easy replacement of existing pipes with
larger sizes.
4. Easy inspection and maintenance of pipes.
655
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
The disadvantages of pipe tunnels over conduits are:
1. Higher first cost.
2. Higher maintenance cost in general.
8 • Is the steam consumption less in a building that shuts off its steam at
night than in one that does not? Why?
It has been thoroughly demonstrated that the steam consumption is less in a building
where the steam is shut off at night. Although therejs, in some cases, an increased con-
sumption of heat when steam is again turned on in the morning, there is a large net
saving which may be explained by the fact that the lower inside temperature maintained
during the night obviously results in lower heat loss from the building, and less heat need
therefore be supplied.
9 • What are the common methods for salvaging heat in condensate?
The most common methods are:
1. The use of a water heating economizer for preheating the hot water supply to the
building.
2. The use of a cooling radiator.
10 • What are the common means used to graduate the heat supply according
to variations in outside temperature?
a. A weather compensating thermostat regulates the steam supply automatically
according to the outdoor temperature, and gives frequent short intervals of inter-
mittent steam supply; at the same time it insures delivery of steam to all the radiators.
b. Another method which is very simple is the use of an ordinary vacuum return line
system in which the pressure in the radiators is varied between a high vacuum and a
few pounds to produce some control over the heat output.
c. The use of an orifice system graduates heat supply.
d. The time-limit control which may be set to provide no service, continuous service, or
periodic service, is also used. For periodic service, steam may be supplied during
each period in increments of a certain number of minutes for each successive setting
of the switch, steam being shut off during the balance of the period. This type of
service is provided by several intermittent settings. A night switch will maintain
the intermittent day setting, or interrupt the day operation and cut off the supply of
steam at night during any desired hours.
656
Chapter 38
RADIANT HEATING
Physical and Physiological Considerations, British Equivalent
Temperature, Control of Heat Losses, Methods of Application,
Principles of Calculation, Mean Radiant Temperature, Measure-
ment of Radiant Heating
HEATING for comfort is generally understood to mean that heat
must be supplied to control the rate of heat loss from the human
body so that the physiological reactions are conducive to a feeling of
comfort in the individual. While in convection heating, as described in
Chapter 30, heat is transferred from a heating unit to the air and thence
to the occupant, the primary object of radiant heating is to warm the
occupant directly without heating the air to any extent. Thus, the
difference between convection heating and radiant heating is partly
physical and partly physiological.
Comfort requires that heat be removed from the body at the same rate
as it is generated by the oxidation of the foodstuffs in the body tissues.
The normal rate of heat production in a sedentary individual is about
400 Btu per hour1, or, since the entire surface area of an average adult is
19.5 sq ft, about 20.5 Btu per square foot per hour. Conditions should be
such as to remove heat at this rate if the surface is to be maintained at the
mean normal surface temperature of the human body.
Heat is transferred from any warm dry body to cooler surroundings
principally by convection and by radiation, the approximate total rate of
heat loss being the sum of the two. Where the body surface is moist there
is additional loss of heat through evaporation from both the body surface
and the respiratory tract.,
The rate of heat loss by convection depends upon the difference between
the temperature of the body and that of the surrounding air, and on the
rate of air motion over the body. The loss by radiation depends entirely
upon the difference between the temperature of the body and the mean
surface temperature of the surrounding walls and objects. This latter
temperature is called the mean radiant temperature (MRT). Because
these two types of heat loss a'ct in a supplementary manner toward each
other, a required rate of heat loss can be secured by having a relatively
low air temperature and a relatively high MRT, or vice versa. Thus, if the
air is reduced from a given temperature to a lower temperature, the
amount of heat lost from the body by convection is increased, and this
lHeat and Moisture Losses from the Human Body and Their Relation to Air Conditioning Problems,
by F. C. Houghten, W. W. Teague, W. E. Miller, and W. P. Yant (A.S.H.V.E. TRANSACTIONS, Vol. 35,
1929).
657
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
increase can be compensated for by raising the MRT. Similarly, with a
higher air temperature the same total heat loss will be maintained by a
correspondingly lower MRT.
The loss by evaporation depends on the air temperature, air movement,
and humidity; it is increased if the humidity is reduced. For the usual
conditions of heating by radiators or convectors, where the air tempera-
ture ranges from 70 F to 73 F, approximately 75 per cent of the total heat
loss of 400 Btu per hour occurs by radiation and convection, and the
balance, or 100 Btu per hour, occurs by evaporation. In the case of
radiant heating, if the air temperature is reduced to 60 F, 84 per cent of
the 400 Btu per hour, or 336 Btu per hour, is lost by radiation and con-
vection, and 64 Btu per hour are lost by evaporation.
The mean normal surface temperature of the human body, taken over
the whole area, including not only the exposed skin surface but also sur-
faces of the clothes and the hair, has been very extensively used as 75 F,
particularly in British literature. However, results obtained by Aidrich2
in rooms in which the air and wall surface temperatures were approxi-
mately 72 F gave mean values nearer to 83 F than to 75 F.
The mean body surface temperature which will maintain the optimum
heat loss by radiation and convection in a uniform environment of 72 F
may be calculated from fundamental equations for radiation and natural
convection by substituting a comparable cylinder for the body. Heilman3
gives the following equations:
-(ro)'] «
('-.-r.r>
where
HT =* heat loss by radiation, Btu per square foot per hour.
He » heat loss by convection, Btu per square foot per hour.
Zs = absolute temperature of the body surface, degrees Fahrenheit.
Tw - absolute temperature of the walls, degrees Fahrenheit.
TV = absolute temperature of the air, degrees Fahrenheit.
m _ „ __
D « diameter of cylinder, inches.
e « the ratio of actual emission to black body emission,
If it be assumed that a normal adult has an average height of 5 ft 8 in.
and an average body surface area of 19.5 sq ft, the surface of his body will
have the same area as that of a cylinder 5 ft 8 in. long with a diameter of
13.15 in* The value of e for skin and clothing is practically 0.95. Ta and
Tw are each taken as 72 F, or 532 Absolute. The surn^ of HT and Hc is
taken to be 15.4 Btu per square foot per hour, which is derived as the
normal rate of heat loss due to convection and radiation from a sedentary
individual by dividing his total sensible heat loss by his area. Solution of
*A study of Body Radiation, by L. B. Aidrich (Smithsonian Miscellaneous Collections, Vol, 81, No. 6,
December, 1928).
•Surface Heat Transmission, by R. H. HeUman (Trans. A*S,M.E.V F#ds and Steam Power
Vol. 51, No. 22, September-December, 1929).
CHAPTER 38 — RADIANT HEATING
Equations 1 and 2, using average figures as outlined, gives a value of
approximately 83 F for the normal temperature of the body surface.
This agrees more closely with the values obtained by Aldrich than with
the 75 F used by British investigators.
British Equivalent Temperature
The British Equivalent Temperature BET is the temperature of an
environment which is effective in controlling the rate of sensible heat loss
from a sizable black body in still air when the body has a maintained
surface temperature of 83 F. The BET is, therefore, a function of both
the air temperature and the mean radiant temperature. Its numerical
value in a uniform environment (walls and air at the same temperature)
is equal to the temperature of the walls and air. In a non-uniform environ-
ment (walls and air at different temperatures) the BET is equivalent to
that of a uniform environment in which an 83 F surface loses sensible
heat at the same rate as it does in the non-uniform environment. As
originally defined, the BET was based on a body surface temperature of
75 F, but 83 F has been accepted as giving results more nearly conforming
with American practice4. The higher the BET the less the heat loss from
the body, the rate of loss in still air being approximately proportional to
the difference between the BET and the mean body surface temperature.
If the BET were 83 F, there could be no sensible heat loss from a
surface at that temperature, so the temperature of a normal body surface
would have to rise to a point where the heat generated in the tissues could
be dissipated.
When convected heat is used, the temperatures of the air and walls are
nearly the same, and the optimum value of the BET from the physio-
logical point of view is 72 F. Under these conditions the mean surface
temperature of a normal body would have the optimum value of 83 F
because the rate of heat loss by radiation and convection would be 15.4
Btu per square foot per hour and that by evaporation 5.1 Btu per square
foot per hour, which would just balance the rate of heat production of
20.5 Btu per square foot per hour. This BET of 72 F in a uniform
environment is exactly equivalent to the effective temperature of 66 F as
defined by the AMERICAN SOCIETY OF HEATING AND VENTILATING
ENGINEERS (see Chapter 2), because, in a uniform environment, a dry-
bulb temperature of 72 F in still air with a relative humidity of 30 per cent
gives an effective temperature of 66 F, which has been determined to be
the optimum.
METHODS OF APPLICATION
There are two general methods of applying radiant heating, as follow:
1, By warming the interior surfaces of the building. Pipe coils are embedded in the
concrete or plaster of the walls, ceiling or floors, the heating medium being hot water or,
in some cases, steam. This has the effect of warming the entire concrete or plaster
surface in which the pipes are embedded. Since the temperature of the heating medium
should not exceed about 120 F on account of the possibility of cracking the plaster, the
^Application of the Eupatfceoscope for Measuring the Performance of Direct Radiators and Convectors
in Terms qf Equivalent Temperatures, by A. C. Willard, A, P, tCrat?, and M. K. Fahnestock (A.S.H.V.E,
Journal, Beating, Piping and Air Conditioning, July, 1933),
6S9
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
area of the panel must be sufficient to supply the requisite quantity of heat at this low
temperature. When carefully designed, this method produces comfortable and eco-
nomical results.
2. By attaching separate heated plates or panels to the interior surfaces of the structure.
These plates or panels are placed either in an insulated recess flush with the surface of
the walls or ceiling or bolted on its face. They may be decorated as desired. As it is
difficult to make an invisible joint between the edge of such a plate and the plaster, it is
common to use a frame of plaster, wood, metal or composition around the panel. These
plates may be placed either on the ceiling or the wall, or in some cases as a margin
around the edge of the floor. If floor heating is required the temperature over the whole
area should not exceed 70 F.
If the entire warm surface is installed at one end of the room there may
be a marked difference between the BET on the two sides of a body in the
room. It is usually desirable therefore that the heat be distributed at
different points in the room so that no uncomfortable effects will be felt
from unequal heating.
PRINCIPLES OF CALCULATION
The calculations for radiant heating are entirely different from those
for convective heating. The purpose of the latter is to determine the rate
of heat loss from the room by conduction, convection, and radiation when
maintained in the desired condition; radiant heating involves the regu-
lation of the rate of heat loss per square foot from the human body.
The first step in the calculations for radiant heating is to ascertain the
necessary mean radiant temperature (MRT) ; next, the size, temperature,
and disposition of the heating surfaces required in the room to produce
this MRT are estimated; and after this the determination of the convec-
tive heat is made.
Mean Radiant Temperature
If the whole of the interior surface of a room were at the same tempera-
ture, this * temperature would represent the MRT. Such a condition
seldom exists, however, since the actual surface temperature in any
heated space having surfaces exposed to the outer air varies greatly for
different sides of the enclosure. It is therefore necessary to ascertain by
calculation the mean of these interior surface temperatures.
The mean temperature in this sense is not the arithmetic average of the
actual thermometric temperatures of the surfaces, but the temperature
corresponding to the average rate of heat emission per square foot of
surface. The temperature corresponding to this mean emission can be
taken from Table L Conversely, the emission at different temperatures
and also the emissivity factors can be obtained from this table. For
instance, 1 sq ft of surface at 50 F will emit 104.9 Btu per square foot per
hour to surroundings at absolute zero if the emissivity of the surface is 0.9.
If the area in square feet of each part of the space is multiplied by the
emission value corresponding to its actual temperature, and these products
are added together, the gross amount of radiant heat discharged into the
room by the wall surface per hour is obtained. This quantity, divided by
the total interior surface, gives the average amount of heat coming into
the room from the surface of the walls per square foot of surface per hour.
Interpolating in Table 1, the total radiation from a surface at 83 F for
660
CHAPTER 38 — RADIANT HEATING
TABLE 1. TOTAL BLACK BODY RADIATION TO SURROUNDINGS AT ABSOLUTE ZEROa
BODY
OR
MEAN
RADIANT
TEMPER-
ATURE
Deg
Fahr
Radiation in Btu per square foot per hour
emitted to surroundings with a tempera-
ture of absolute zero by bodies at various
temperatures and with emissivity factor e
BODY
OR
MEAN
RADIANT
TEMPER-
ATURE
Deg
Fahr
Radiation in Btu per square foot per hour emitted
to surroundings with a temperature of absolute
zero by bodies at various temperatures and
with emiesivity factor e
€
1.00
0.9S
0.90
0.80
e
1.00
0.95
0.90
0.80
30
99.3
94.3
89.4
79.4
71
136.5
129.6
122.9
109.3
35
103.5
98.3
93.2
82.8
72
137.4
130.5
123.6
109.9
40
107.6
102.4
96.8
86.1
73
138.4
131.5
124.5
110.6
45
112.1
106.5
100.9
89.7
74
139.6
132.6
125.6
111.7
46
112.9
107.3
101.6
90.4
75
141.0
133.9
126.9
112.8
47
113.9
108.2
102.5
91.1
80
146.6
139.4
132.0
117.4
48
114.8
109.1
103.4
91.9
85
152.3
144.6
137.1
121.9
49
115.6
109.9
104.1
92.4
90
157.9
149.9
142.1
126.4
50
116.5
110.6
104.9
93.2
100
169.6
161.1
152.6
135.7
51
117.5
111.6
105.8
94.0
110
181.6
172.5
163.5
145.4
52
118.4
112.5
106.5
94.7
120
194.8
185.0
175.4
155.9
53
119.4
113.4
107.4
95.5
130
210.1
199.6
189.1
168.1
54
120.2
114.2
108.2
96.2
140
223.2
212.1
201.0
178.5
55
121.1
115.1
109.0
96.9
150
237.1
225.2
213.5
189.7
56
122.1
116.0
109.9
97.7
160
251.1
238.8
226.0
201.0
57
123.1
117.0
110.9
98.5
170
270.5
257.0
243.5
216.4
58
124.0
117.8
111.6
99.2
180
288.0
273.8
259.1
230.4
59
124.9
118.6
112.4
99.9
190
306.5
291.0
275.8
245.1
60
125.8
119.5
113.4
100.7
200
325.2
309.0
292.8
260.3
61
126.6
120.3
114.0
101.4
210
348.0
330.6
313.1
278.4
62
127.7
121.4
114.9
102.2
220
371.5
353.0
334.4
297.1
63
128.6
122.2
115.8
102.9
250
437.8
415.9
394.0
350.2
64
129.6
123'. 1
116.7
103.7
300
575.0
546.1
517.5
460.0
65
130.5
124.0
117.5
104.4
350
740.0
703.0
666.0
592.0
66
131.6
125.0
118.4
105.4
400
942.1
895.0
847.5
753.5
67
132.5
125.9
119.3
106.0
450
1176.0
1117.0
1059.0
941,0
68
133.5
126.8
120.1
106.8
500
1464.0
1390.0
1318.0
1171.0
69
134.5
127.8
121.1
107.6
550
1791. D
1701.0
1613.0
1434.0
70
135.5
128.8
121.9
108.4
600
2405.0
2284.0
2165.0
1925.0
aThese factors are calculated from the formula
0.1723 X T* \
, 100,000,000 )
where
Q •• total black body radiation, Btu per square foot per hour.
e •" emisaivity,
T «* absolute temperature, degrees Fahrenheit.
an emissivity of 0.95 is 142 Btu per square foot per hour. The difference
between 142 Btu and the average amount of heat coming into the room is
the amount which will be lost per square foot per hour by radiation from
a body at 83 F. If a rate at which it is desired that heat be lost from the
body by radiation and convection be assumed, the mean radiant emission
from the walls required to give the desired result can be determined from
Table. 1, as can also the required air temperature for the corresponding
convective effect,
The determination of the amount of radiant heating surface needed in
a room requires knowledge of the climate, the type of structure, the type
of heating, and the surface temperature of the walls. This problem can
be solved only on an empirical basis. After some experience, however,
661
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
it is possible to estimate these variables with a considerable degree of
accuracy for any climate or construction.
Assume that a mean radiant temperature of 65 F is desired. Table 1
shows that with all the walls at this temperature, and with an emissivity
of 0.95, the gross heat emission is 124 Btu per square foot per hour. The
total emission of radiation into the room from that surface would there-
fore be A X 124, where A is the total inside area of the room. This is the
desired emission.
If the whole area be divided into a number of different parts which are
each at a uniform temperature — ai, as, as, — and each is multiplied by the
value of the heat emission corresponding to that temperature, and if all
these products are added together, their sum will represent the total
actual emission of radiation into the room at these temperatures without
the aid of any hot surface.
The difference between the desired emission and the actual emission
represents the additional heat which must be supplied by the hot surface.
The temperature of the proposed hot surface must then be selected, and
its emission per square foot at that temperature determined from Table 1.
This emission is divided into the additional amount of heat needed, ad-
justed for the fact that the heating units will shield the walls behind
them, and the quotient obtained will be the area of the required heating
surface.
It is evident that this method of calculation is approximate, and
depends for its accuracy on a correct estimate of the ultimate surface
temperatures attained by the actual wall surfaces.
It is necessary also to calculate how much heat will be given off by the
same surfaces by convection, and thereby to determine ^ whether this
amount of convected heat will warm entering ventilating air to the tem-
perature maintained. If it will not, additional convection surfaces must
be introduced to make up the deficiency.
MEASUREMENT OF RADIANT HEATING
Convection heating, having as its object the raising of the air tempera-
ture to a specified degree, must be measured by thermometric methods
which indicate essentially the air temperature, and not the rate of heat
loss from the human body. Radiant heating, having as its object the
control of the rate of heat loss from the human body, ^ can be measured
only by methods which basically are calorirnetric, that is, which measure
directly the rate of heat loss from an object maintained at the temperature
of the body, irrespective of air temperature.
The apparatus for this purpose consists essentially of a hollow sphere,
or cylinder, containing a fluid which can be maintained accurately at 83 F
(the accepted mean surface temperature of the human Jbody), with an
accurate means of measuring the rate of heat supply required to maintain
the temperature at that exact point. The latter measurement can be
made with sufficient accuracy by electrical methods, Although a BET of
72 F is desirable, the mean radiant and air temperatures may both vary,
provided the heat loss by radiation and convection from a surface at
83 F is maintained at the rate of 15.4 Btu per square foot per hour,
662
CHAPTER 38 — RADIANT HEATING
15 4
which corresponds to O^TK = ^.5 watts per square foot of exposed
surface.
This instrument, the eupatheoscope, can readily be adapted as a thermo-
stat by electrical control to shut off or turn on heat when the critical
temperature of 83 F in the vessel is increased or decreased. A modifi-
cation of the instrument is called the eupatheostat.
Another instrument for maintaining comfort conditions is at present
available only in a model adapted to British practice as it is designed for a
temperature of 75 F. It consists of a blackened copper sphere of approxi-
mately 6 in. diameter in which is housed a cylindrical sump containing a
volatile liquid. In operation, a small electric heating coil drawing about
5 watts creates in the sphere a vapor pressure which is constant as long as
the heat losses from the sphere are standard. If the temperature of the
air or the MRT becomes too high for comfort, a greater pressure is
created, owing to a smaller loss of heat from the sphere. This increase of
pressure acts on a diaphragm and shuts off the supply of heat to the room.
For testing work, the globe thermometer is a very useful instrument. It
consists of an ordinary mercury thermometer, with its bulb placed in the
center of a sphere from 6 in. to 9 in. in diameter, usually made of thin
copper and painted black. The temperature thus recorded is termed the
radiation-convection temperature .
EXAMPLE
Example L The surface areas, temperatures, and emissions for a room having a
volume of 5760 cu ft are given in Table 2. The figures for temperatures are fairly
representative of American practice with well-built walls, and are based on an emissivity
of 0,95 which approximates that of most paints and building materials.
TABLE 2. SURFACE AREAS, TEMPERATURES, AND EMISSIONS FOR A ROOM OF 5760 Cu FT
ARBJA
SQFT
ASSUMED SURFACE
TBMPHRAXUKB
(DJSG FAHR)
HIAT EMISSION
(BTtr PER SQ FT
PER HOTO)
TOTAL HEAT EMISSION
FROM AREA
(B<pu PBH HOUR)
External Wall
297
50
110.6
32,850
Glass
279
45
106.5
29,710
Inner Wall
480
55
115.1
55,250
Ceiling..... „
480
55
115.1
55,250
Floor
480
55
115.1
55,250
Total,..,
2016
228,310
The mean radiant temperature of the room is
228,310
2016
113.2 Btu per square foot
per hour which, as seen from Table 1, corresponds to an MRT of 53 F for an average
emissivity of 0.95*
For an average individual having a body surface of 19.5 sq ft, under conditions of
comfort with a body surface temperature of 83 F, the heat given off by radiation may be
determined by means of Equation 1 as 217 Btu per hour, or 11.1 Btu per square foot per
hour. This corresponds to an environmental emission of 142 — 11.1 » 130.9 Btu per
square foot per hour, and, according to Table 1, to an MRT of 72 F.
If this body be placed in the room described, it will lose heat at the rate of 19.5
(142 — 113.2) « 562 Btu per hour. This loss is 345 Btu per hour, or 17.7 Btu per square
loot pet hour, more than the rate of heat loss for comfort, wfyich is only 19.5 (142 — 130.9)
« 217 Btu per hour.
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
In order to determine the amount of radiating surface necessary to maintain the MRT
at 72 Fr assume the surface temperature of the hot plates to be installed to be 200 F,
which is approximately the temperature they would have if heated by steam.
The 2016 sq ft total area of the surfaces of the room multiplied by 130.9, which is the
emission in Btu per square foot per hour necessary to maintain a body surface tempera-
ture of 83 F, gives a total desired emission of 263,890 Btu per hour. It is necessary to
supply enough radiant heating surface to increase the total actual mean radiant heat
emission by the room from 228,310, as shown in Table 2, to the 263,890 Btu desired.
The additional heat needed is the difference between these figures, or 35,580 Btu. Since,
from Table 1, the emission per square foot at 200 F is 309 Btu, the required radiant
o K c QA
heating surface needed is 'nn = 115 square feet. The effect of this surface suitably
ouy
placed would be to raise immediately the mean radiant temperature to the required
degree and to maintain it at that value as long as the surfaces remained at the values
assumed.
In the solution of this particular example, the radiation loss from the
human body was selected as 217 Btu per hour, which is that taking place
under optimum comfort conditions, with a body surface temperature of
83 F in a uniform environment at 72 F. The mean radiant temperature
necessarily was 72 F. If the optimum BET of 72 deg Fahr is desired,
an air temperature of 72 F also must be maintained. If it is desired to
maintain a lower air temperature than this, a mean radiant temperature
greater than 72 F must be selected and the radiation loss from the in-
dividual must be recalculated from Equation 1.
The calculation may be simplified by preparing tables showing, at the
usual temperatures, the area of hot surface required to bring each square
foot of actual wall surface at various temperatures up to a general
standard of from 60 F to 70 F. It would then be necessary only to
multiply the respective areas by the appropriate factors, and to add the
results, to obtain the required total.
REFERENCES
Room Warming by Radiation, by A. H. Barker (A.S.H.V.E. TRANSACTIONS, Vol. 38,
1932).
Panel Warming, by L. J. Fowler (A.S.H.V.E. TRANSACTIONS, VoL 36, 1930).
Calculations for Radiant Heating, by T. Napier Adlam (Heating and Ventilating,
October, 1931).
Principles of Calculation of Low Temperature Radiant Heating, by A. H. Barker
(Proceedings of The Institution of Heating and Ventilating Engineers, London, VoL 30,
1931).
Application of the Eupatheoscope for Measuring the Performance of Direct Radiators
and Convectors in Terms of Equivalent Temperatures, by A. C. Willard, A. P, Kratz
and M. K- Fahnestock (A.S.H.V.E. Journal Section, Heating, Piping and Air Con~
ditioning, July, 1933).
What will be the Future Development of Heating and Air Conditioning, by W. H.
Carrier (Heating, Piping and Air Conditioning, January, 1933).
Method of Installing the Panel Heating System in the British Embassy Building
(Heating, Piping and Air Conditioning, July, 1934).
Panel Heating, by C. M. Gates (Proceedings of Institution of Heating and Ventilating
Engineers, London, Vol. 30, 1931).
Notes on Electric Warming with Special Reference to Low Temperature Panel
Systems, by R. Grierson (Proceedings of Institution of Heating and Ventilating Engineers,
London, Vol. 28, 1929).
Radiant Heat,*by A. F. Dufton (Proceedings of Institution of Heating and Ventilating
Engineers, London, VoL 30, 1931).
Radiant Heat, by A. F. Dufton (Proceedings of Institution of Heating and Ventilating
Engineers, London, VoL 31, 1932).
Notes on the Theory of Radiant Heating, by C, G. Heys Hallett (Proceedings of
Institution of Heating and Ventilating Engineers, London, VoL 29, 1930).
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CHAPTER 38 — RADIANT HEATING
PROBLEMS IN PRACTICE
1 • Name three ways that heat is lost from the human body.
By radiation, convection, and evaporation.
2 • What is the mean normal surface temperature of the human body as
determined for the United States?
83 F.
3 • What is the exact purpose of radiant heating?
Radiant heating regulates the heat loss from the human body.
4 • How is the required amount of radiant heating surface found?
By calculating the desired emission and the actual emission, and finding their difference.
This is additional heat which must be supplied by the hot surface.
5 • After finding the required heat, how is the necessary hot surface area
calculated?
Having selected the hot surface temperature, find the emission per square foot from
Table 1. This rate divided into the heat required gives the area of the necessary heating
surface.
6 • Is the heat generated in the body affected by action? If so, does it vary
greatly?
Yes. With hard work or energetic exercise, the total heat generated in the body may be
five to six times that generated when it is at rest.
7 • When and why does the human body feel cold?
The body feels cold not only when it loses heat at a greater rate than it can generate it,
but also when heat is abstracted from the body disproportionately. The human body
does not require any heat from without because it generates more heat than is sufficient
to maintain the correct temperature; therefore, it is only necessary to provide conditions
that will maintain the correct ratio of losses.
8 • a. Where did radiant heating derive its name?
b. What is actually meant by radiant heating?
a. The term radiant heaters was introduced about 25 years ago to designate flat heating
surfaces made to give off practically all their heat by radiant ether waves instead of
relying on convected warm air.
b. The term radiant heating now applies to methods of heating where, instead of heating
the air to a predetermined temperature, flat heating surfaces are so placed in a room
that the average virtual temperature of all wall, ceiling, floor, and glass surfaces
exposed to the body is just sufficient to prevent the body's losing too much heat by
radiation. The air temperature can be much cooler with radiant heating because
radiation losses from the body are compensated.
9 • What kind of heating surfaces are in general use?
The heating units may have flat iron surfaces heated with steam and placed under
windows, or hot water pipes may be embedded in the floor, walls, or ceilings. Electrical
radiant heaters are made by embedding resistance elements in porcelain or electric
conductors woven into a thick paper which can be fastened to the walls or ceilings.
10 • What kind of heat rays are commonly generated in radiant heating?
Give examples.
All heat rays are generally assumed to be the same as light rays; they travel at the speed
of light, but they are invisible and loneer. The rays used in heating are 0.00005 to
0.0001 in. long compared with visible red rays of about 0,000027 in.
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
11 • What natural evidence have we that air temperature alone is no criterion
of comfort and that radiant heat affects the body more quickly?
When standing in the sunshine on a cool spring day, a person feels perfectly comfortable,
but when a cloud passes over the sun, he instantly feels much cooler as the shadow
reaches him. A shielded thermometer recording the temperature of the air shows no
reduction in air temperature in so short a period, so that the person actually feels a
sensation of cold which an ordinary thermometer cannot register. This shows that
light and heat rays are shut off simultaneously and travel at the same speed; it also
proves that radiant rays affect the comfort of the body quicker than air temperature
does.
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Chapter 39
ELECTRICAL HEATING
Resistors, Heating Elements, Electric Heaters, Unit Heaters,
Central Fan Heating, Electric Steam Heating, Electric Hot Water
Heating, Heat Pump, Control, Calculating Capacities, Power
Problems, Electric Heating Data
TTLECTRIC heating has a logical and a rapidly growing place in the
XL/ heating industry because of its advantages of flexibility, cleanliness,
safety, convenience, and ease of control. Electric heating practice has
many basic principles in common with fuel heating, but there are also
important differences. The advantages of good building insulation are
even more important in electric heating than for fuel heating, because the
initial cost per Btu is usually higher.
All heat is a form of energy. Fuels hold stored chemical energy which
is released into heat by combustion. Electrical power is a form of energy
which can be released into heat by passing it through a resisting material.
Both fuel and electric heating have two divisions: first, the conversion of
energy into heat; second, the distribution and practical use of the heat
after it is produced.
In converting the chemical energy of fuels into heat by combustion,
there is necessarily a considerable variation in thermal efficiency. This
is not true, however, when converting electric power into heat, because
100 per cent of the energy applied in the resistor is always transformed
into heat. In electric heating practice the engineer need not be concerned
about efficiencies of heat production, but rather about efficiencies of heat
utilization.
DEFINITIONS
Definitions of terms used in fuel heating are given in Chapter 41. The
following terms apply particularly to electric heating:
Electric Resistor ; A material used to produce heat by passing an electric current
through it. *
Electric Heating Elements A unit assembly consisting of a resistor, insulated
supports, and terminals for connecting the resistor to electric power.
Electric Heater: A complete assembly of heating elements with their enclosure,
ready for installation in service.
RESISTORS
Solids, liquids^ and gases may be used as resistors, but most com-
mercial electric heating elements have solid resistors, such as metal
alloys, and non-metallic compounds containing carbon. In some types of
electric boilers, water forms the resistor which is heated by an alternating
currerit of electricity pa&stog through it. One of the more common
eer
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
resistors is nickel-chromium wire or ribbon which, in order to avoid
oxidation, contains practically no iron.
HEATING ELEMENTS
Commercial electric heating elements are divided into open type
elements, enclosed type elements, and cloth fabrics. Open type elements
have resistors exposed to view. The resistors may be coils of wire or
metal ribbon, supported by refractory insulation, or they may be non-
metallic rods, mounted on insulators. Open type elements are used
extensively for operation at high temperatures when radiant heat is
desired. They are also frequently used at low temperatures for convec-
tion and fan circulation heating, especially in large installations.
Enclosed type elements have metallic resistors embedded in a refractory
insulating material, and encased in a protective sheath of metal. Fins or
extended surfaces may be used to add heat-dissipating area. Enclosed
elements are made in many forms, such as strips, rings, plates, and tubes.
Strip elements are used for clamping to surfaces requiring heat by con-
duction, and in convection and fan circulation air heaters. Ring and
plate elements are used in electric ranges, waffle irons, and in many small
air heaters. Tubular elements may be immersed in liquids, cast into
metal, and, when formed into coils, used in electric ranges and air heaters.
Cloth fabrics woven from flexible resistor wires and asbestos thread, are
used for many low temperature purposes.
ELECTRIC HEATERS
Electric heaters are classified according to the manner in which they
deliver heat in practical use, that is, by conduction, by radiation, or by
convection. The term radiator should not be used in electric heating,
because of confusion between its established usage in fuel heating and the
radiant principle of many electric heaters.
Among the uses of conduction electric heaters, which deliver most of their
heat by actual contact with the object to be heated, are aviators' cloth-
ing, hot pads, foot warmers, soil heaters, ice melters, and pipe heaters.
Conduction heaters are useful in conserving and localizing heat delivery
at definite points. They are not suitable for general air heating.
Radiant electric heaters, which deliver most of their heat by radiation,
have high temperature incandescent heating elements and reflectors to
concentrate the heat rays in the desired directions. The immediate and
pleasant sensation of warmth which is caused by radiant heat makes this
type desirable for temporary use where the heat rays can fall directly
upon the body. They are not satisfactory for general heating, as radiant
heat rays do not warm the air through which they pass. They must
first be absorbed by walls, furniture, or other solid objects which then
give up the heat to the air. The location of radiant heaters is important.
They should never face a window because some rays would pass through
the glass and be lost. Figs. 1 and 2 show common types of portable and
wall-mounted radiant heaters.
Convection electric heaters, designed to induce thermal air circulation,
deliver heat largely by convection, and should be located and used in
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CHAPTER 39 — ELECTRICAL HEATING
much the same manner as steam and hot water radiators or convectors.
They should have heating elements of large area, with moderate surface
temperature, enclosed to give proper stack effect to draw cold air from
the floor line (Figs. 3 and 4). The flexibility possible with electric heating
elements should discourage the use of secondary mediums for heat
transfer. Water and steam add nothing to the efficiency of an electric
heater and entail expensive construction.
UNIT HEATERS
Fan unit electric heaters, having electric heating elements combined in
the same enclosure with a fan or blower, are made in many styles and are
excellent for general air heating. They should be located and used much
FIG. 1.
PORTABLE RADIANT ELECTRIC
HEATER
FIG. 2. RADIANT ELECTRIC HEATER
RECESSED IN WALL
t
I
FIG. 3.
CONVECTION ELECTRIC HEATER
ON WALL SURFACE
FIG. 4.
CONVECTION ELECTRIC HEATER
RECESSED IN WALL
as steam unit heaters. The warm air can be directed toward the floor, if
desired, to give a positive circulation which will reduce stratification of
air. Small units which are free from radio interference are used for
homes; there are large units for industrial plants, substations, power
houses, and pumping stations; portable units are useful for temporary
work, such as drying out damp rooms, or for warming rooms during
construction (Figs. 5, 6, 7 and 8).
CENTRAL FAN HEATING
Central fan electric heating systems have electric heating elements and
fans or blowers to circulate the air through ducts, and in addition to the
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
main heaters at the fan location, booster heaters may be located in branch
ducts. Humidification or complete air conditioning can readily be in-
cluded in the system, in much the same manner as with steam.
In coordinating the input of heat energy and the volume of air circu-
lation, a basic difference between electric heating and steam heating
enters into the problem. Steam is approximately a constant-temperature
source of heat for any given pressure as a change in air volume flowing
over steam coils does not greatly affect the temperature of the delivered
air. The amount of steam condensed (heat input) varies in proportion to
the air volume, but the surface temperature of the steam coils remains
FIG. 5. SMALL PORTABLE FAN UNIT
ELECTRIC HEATER
FIG. 6. LARGE INDUSTRIAL TYPE PORT-
ABLE FAN UNIT ELECTRIC HEATER
r t t
FIG. 7.
SMALL FAN UNIT ELECTRIC
HEATER
FIG. 8, LARGE INDUSTRIAL TYPE FAN
UNIT ELECTRIC HEATER
about the same. Electric heat is quite different, being a constant source
of energy. If the volume of air flow over electric heating elements is
changed, and no change is made in the electrical power connections, there
will be a corresponding change in the temperature of the air delivered
because the electrical energy input remains constant and the surface
temperature of the heating elements will vary as is necessary to force the
air to accept all the heat. With electric heat the total heat is constant
unless some compensating action is performed by control. Automatic
modulation to vary the electrical heat input and synchronize it properly
with the air flow has been successfully applied to central fan systems*
ELECTRIC STEAM HEATING
Electric steam heating differs from fuel heating only in the use of electric
boilers to generate steam. Small boilers usually have heating elements
of the enclosed metal resistor type immersed in the water. Boilers of this
construction may be used on either direct or alternating current since the
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CHAPTER 39 — ELECTRICAL HEATING
heat is delivered to the water by contact with the hot surfaces. To lessen
the likelihood that the heating elements will burn out, they are made
removable for cleaning off deposits of scale which will restrict the heat
flow. Boilers of this type are useful in industrial plants which require
limited amounts of steam for local processes, and for sterilizers, jacketed
vessels, and pressing machines which need a ready supply of steam.
Electric boilers are entirely automatic and are well adapted to inter-
mittent operation. It frequently is economical to shut down the main
plant boilers when the heating season ends, and to supply steam for
summer needs with small electric boilers located close to the operation.
Large electric boilers are usually of the type employing water as the
resistor. Only alternating current can be used, as direct current would
cause electrolytic deterioration. Large boilers of this kind have electrodes
immersed in the water where heat is generated directly. In Canada and
Europe many successful installations have been made, but in the United
States the cost of electric power, in comparison with fuels, does not favor
its general use.
ELECTRIC HOT WATER HEATING
Electric hot water heating offers an extremely convenient and reliable
means of supplying all needs for hot water, and in sections of the country
where low current rates have made it economically feasible, it enjoys
popularity. Electric boilers for hot water heating are inexpensive,
entirely automatic, and are insulated to prevent excessive heat losses.
When lower power costs can be secured, by confining the heating to
certain fixed hours, water may be heated and stored^ in well-insulated
tanks for use when needed. In large industrial plants it is often possible
to balance power loads by this means and to avoid running the fuel-fired
steam boilers at night or over week ends. In Europe use has been made of
this hot water storage principle for heating. Experiments have been
made in this country for heating houses, but the cost of serving individual
homes with the necessary heavy electric power loads has proved un-
profitable at rates comparable to other forms of heating. The problems
incident to installing large storage tanks in home basements, and the lack
of flexibility under variable weather conditions, are also unfavorable
factors.
OIL HEATING
Electric hot oil heating is useful in some industrial work as a substitute
for superheated steam. Special oil can be electrically heated as high as
600 F and pumped at a pressure just sufficient to cause flow. When used
in heating coils or jacketed vessels, this gives a safe, and convenient,
automatic system for moderate-sized installations.
HEAT PUMP
The electric heat pump is not strictly an electric heater, as it does not
directly convert electrical power into heat. It operates a compressor
electrically which acts as a reversible refrigerating unit to ^extract heat
from the outdoor air in winter and deliver it indoors for^heating purposes,
and, by a reversal, to extract heat from the indoor air in summer and
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
discharge it outdoors. This system has been used in evenly-balanced
climates where the heating requirements in winter are about the same as
the cooling requirements in summer.
AUXILIARY ELECTRIC HEATING
In conjunction with heating systems of other types, an auxiliary elec-
trical heating arrangement is a convenient means of caring for mild days
in the spring and fall which require little heat to make a house or building-
comfortable. Likewise, such electrical heating might be used on ab-
normally cold days to help out the main heating system and by this means
reduce the necessary size of the system.
Because of the feeling of comfort that a radiant type heater gives,
bathrooms may be heated electrically with this type of heater while the
rest of the house is cared for by some other system. Offices and rooms
which require heat at periods when the main heating plant is shut down
are conveniently cared for electrically.
CONTROL
Because the efficiency of electric heat production is the same for large
or small units, it is possible to reduce heat waste to a minimum by apply-
ing local heating, locally controlled. Wherever radiant heaters are used,
thermostats are not an effective means of control and manual operation
or control by eupatheoscope is necessary. For all convection and fan
circulation heaters thermostatic control is useful. For small heaters
having ratings up to about 1500 watts, there are direct-acting thermostats
which are satisfactory, but for larger heaters it is advisable to use relays
or contactors, which should break all of the power lines. All heaters
having fan circulation should have the heat circuit interlocked with the
motor circuit so that the fan will be running when the heat is on. A
thermal fuse or trip should be located in the heat chamber to throw off
the heat in case any interruption of air flow should occur; otherwise
undue temperature rise would result. In all large heaters the heating
elements should be arranged in groups and control provided to vary the
heat input to correspond approximately to the heat demand. If this is
not done, and all the heat is kept available, the thermostat will continue
throwing it on and off at short intervals. Except for central fan systems,
the heat stages can be operated by manual switches, but automatic
modulation of the heat load is usually preferred.
CALCULATING CAPACITIES
The methods of calculating heat losses outlined in Chapters 6, 7, and 8
may be used for electric heating exactly as for fuel heating. The total
heat requirements in Btu per hour may then be converted into the
electrical rating of an equivalent heating system by using the equation :
Total Btu per hour , , . , f . - ,„.
„..„„._;._. __ _ kw ratmg of required electric heating (1)
The following empirical rules for estimating electric heater require-
672
CHAPTER 39 — ELECTRICAL HEATING
ments may be used in territories where the heating load is never greater
than 1500 degree days:
Capacity of heater required for average room in home 2 watts per cubic foot.
Capacity of heater required for average office occupied
in the daytime only 1.2 watts per cubic foot.
POWER PROBLEMS
The first point to determine is the cost of the power which is available
for electric heating. Unlike fuels, there is no uniform cost for electric
power because of the unequal cost of distribution to large and small
users. The fact that electricity cannot be economically stored, but must
be used as fast as it is generated, makes it impossible to operate power
plants at uniform loads ; hence, even the time of use may affect the cost of
power.
Homes are almost universally supplied with lighting current of 115
volts, which cannot be used economically for any but the smallest heaters.
Usually the service lines will not permit more than plug-in devices. The
underwriters permit heaters of 1250 watts to be used from approved
baseboard receptacles. Where homes have 230 volt service for cooking
and water heating, and rates are favorable, larger heaters can be installed.
For industrial purposes, heaters should be designed to use polyphase
power, which is usually supplied at 230, 460 or 575 volts. All polyphase
heaters should be balanced between phases.
ELECTRIC HEATING DATA
Electric heater capacity is rated in kilowatts (kw). Electric energy is
measured in kilowatt-hours (kwhr). Cost of operation = kw rating
X hours used X cost per kwhr.
One boiler horsepower (bhp) — 33,471.9 Btu per hour,
One kilowatt-hour (kwhr) = 3,415 Btu.
33 471 9
One boiler horsepower » 0>/I1 ' = 9.80 kwhr.
0,4:10
One boiler horsepower will evaporate 34.5 Ib water per hour /row and at 212 F.
34 5
One kilowatt-hour = Q~^~O = 3.52 Ib of water per hour at 212 F.
Additional conversion factors are given in Chapter 41.
PROBLEMS IN PRACTICE
1 • Why is electrical energy economically feasible to use for certain heating
applications?
a. Because heat from the radiant type of electrical heater is effective in producing com-
fort for the occupant almost as soon as it is turned on, the heater may be turned off
when the room in unoccupied.
6. There is nothing to freeze in an electrical heater.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
c. Electrical energy may be purchased at lower rates during off-peak periods and stored
as heat in water kept in insulated tanks until needed.
d. There is no wasted energy up the flue or in the ash as with fuel heating.
2 • To what localities is electrical heating adaptable?
To those localities where the heating season is relatively mild and where electrical
energy is available at low cost, as in communities served by large hydro-electric plants.
3 • Approximately how low must the rates be to permit the use of electricity
for heating purposes?
Probably the energy must sell for 2 cents or less per kwhr. At 2 cents the cost would be
$5.86 per 1000 Mbh. (See Chapter 29 for comparison with other fuels.) ^ This looks
high, but the seasonal energy consumption would not be as large with electricity as with
other fuels, for reasons stated in Question 1.
4 • Why is automatic control important in connection with electrical heating?
The higher cost of the energy makes it essential that none be wasted.
5 • In fan heating systems, what is an important difference between a steam
heated coil and an electrically heated coil?
A coil supplied with steam at constant pressure will remain at constant temperature
regardless of • the amount of air passing over it. The temperature of the electric coil
supplied with a constant amount of energy will rise if the air quantity is decreased and
fall if the air quantity is increased.
674
Chapter 40
TEST METHODS AND INSTRUMENTS
Pressure Measurement, Temperature Measurement, Air Move-
ment, Humidity Measurement, Carbon Dioxide Determination,
Dust Determination, Flue Gas Analysis, Measurement of Smoke
Density, Heat Transmission, Eupatheoscope
A TMOSPHERIC pressure is usually measured by a mercurial barom-
-/TL eter which, in its simplest form, consists of a glass tube about 3 ft
long, closed at the upper end, filled with mercury and inverted in a
shallow bath of mercury. The pressure of the atmosphere on the exposed
top of the mercury in the cistern supports a column of mercury in the
tube to a height of about 30 in. Readings are taken of the height of the
column between the levels of mercury in the tube and in the cistern.
Atmospheric pressure is the same as the pressure exerted by this supported
column of mercury, and, in pounds per square inch, is equal to its height
in inches times 0.491, which is the weight in pounds of 1 cu in. of mercury.
At latitude 45 deg and sea level, and at a temperature of 32 F, the atmos-
phere will support a column of mercury 29.921 in. in height. The pressure
of 14.7 Ib per square inch, derived by multiplying 29.921 by 0.491, is
called standard or normal barometric pressure. Since the height of the
barometer depends on the density of the mercury as well as on the pres-
sure of the atmosphere, and since the density is dependent on the tem-
perature, mercurial barometer readings should always be corrected for
temperature. An aneroid barometer contains no liquid; it is portable but
less accurate than the mercurial barometer. Atmospheric pressure in
bending the thin corrugated top of a partially exhausted metallic box, or
in distorting a thin-walled bent tube of metal, is made to move a pointer.
Pressures above or below atmospheric are usually measured by means
of gages which indicate the difference between the pressure being measured
and atmospheric pressure at the same time and place. A, gage which
indicates pressures higher than atmospheric is known as a pressure gage,
and a gage which indicates pressures lower than atmospheric is known as a
vacuum gage. The most common type of these gages contains a flexible
hollow brass tube of oval cross section, known as a 3 our don tube. When
subjected to unequal inside and outside pressures, this tube tends to
straighten out, and a pointer motivated by this straightening indicates
the pressure difference on a suitably graduated scale.
High vacuum readings such as are encountered in condenser and steam
jet refrigeration practice are commonly obtained by the use of mercury
column vacuum gages. When the readings obtained with the mercurial
barometer and those with the mercury vacuum gage have both been
corrected to 32 F, the difference in the two readings will give the absolute
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
vacuum in inches of mercury. The following equation may be used to
make corrections for temperature:
h = hi [1 - 0.000101 (ti - t)\
where
h = height of mercury column corrected to temperature t.
Jh = actual height of mercury column.
ti = actual temperature of mercury column.
t = temperature to which column is to be corrected.
A gage which indicates pressures slightly above or below atmospheric is
known as a draft gage. It is essentially a U tube containing either water,
kerosene, alcohol, or mercury, with one leg exposed to the air and the
other connected to a point where the pressure is to be determined. When
the pressure being read is equal to atmospheric, the level of the liquid in
the legs will be the same, indicating a zero gage pressure. When a pres-
sure is applied to one leg, one side will fall and the other will rise an equal
amount. The difference in height between the two liquid levels indicates
the pressure expressed in inches of liquid used in the gage.
TEMPERATURE MEASUREMENT
In engineering work, mercurial thermometers are largely employed to
measure the intensity of heat. These depend on the uniform expansion of
mercury to indicate changes in temperature. An amount of mercury held
in a sealed tube with a bulb at one end will rise to one definite level when
immersed in melting ice, and to another definite level when immersed in
boiling water. These two points are marked, and the space between them
is divided into a number of equal portions, each of which is called a
degree. In the Fahrenheit scale, there are 180 degrees thus obtained,
while the centigrade scale has 100 and the Reaumur has 80. Like divisions
are marked off on the column above and below these two determined
points in order that a greater range of temperature may be read.
Thermocouples1 may be used to measure any range of temperatures up
to 2,900 F, When two dissimilar metals are joined at two points and a
temperature difference exists between these junctions, an electromotive
force will be developed. Its magnitude depends on the composition of the
wires and the difference in temperature between the junctions. A poten-
tiometer or sensitive galvanometer of high resistance connected to the
thermocouple will give a deflection which is a function of the temperature
difference between the hot and cold junctions. Thermocouples con-
nected in series are called thermopiles. Thermocouples for the measure-
ment of high temperatures are calibrated with the aid of the known
melting points of pure metals.
Resistance thermometers are suitable for temperature measurements up
to 1800 F. These thermometers depend for their operation on the change
of resistance with temperature of a platinum, nickel, or copper wire coil,
and they are calibrated in the same way as thermocouples.
»See A.S.H.V.E. research paper entitled Study of the Application of Thermocouples to the Measurement
of Wall Surface Temperatures, by A. P, Jtratz and E. L, Broderick (A.S.H.V.E, TRANSACTIONS, Vol. 38,
1932).
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CHAPTER 40 — TEST METHODS AND INSTRUMENTS
For temperatures above 500 F various types of pyrometers are employed.
The mercurial pyrometer is a thermometer with an inert gas, such as
nitrogen or carbon dioxide, above the mercury column to prevent the
mercury from boiling. The radiation pyrometer consists of a thermopile
upon which the radiation from a hot source is focused by a concave mirror.
A sensitive galvanometer with a calibrated temperature scale indicates
the thermo-electromotive force created by the heat on the thermopile.
The optical pyrometer measures radiant energy by comparing the intensity
of a narrow spectral band, usually red light emitted by the object, with
that emitted by a standard light source (electric lamp) . Thermo-electric
pyrometers operate on the same principle as thermocouples. When
measuring high temperatures, it is customary to hold the cold junction at
room temperature and this may cause some error if the room temperature
is above or below the calibration point. For extremely precise tempera-
ture measurements, the cold junction is usually immersed in melting ice
to fix the cold junction temperature. Various forms of hand-operated and
automatic cold junction temperature compensators are also available.
In the measuring of room temperatures care must be exercised to pre-
vent the results from being affected by the body heat of the observer,
by drafts from doors, windows and other openings, or by radiant heat
from some local source such as a radiator or wall. All thermometers
should be mercury thermometers with engraved stems. The total gradua-
tions of the thermometers should be from 20 to 120 F, in one degree
graduations. No ten, degrees should occupy a space of less than one-half
inch. The accuracy throughout the whole scale must be within one-half
degree. The operator should take hold of the top and no part of the body,
including the hand, should be nearer than 10 in. to the bulb. The
thermometer should not be closer than 5 ft to any door, window, or other
opening; should not be closer than 12 in. to any wall; and should be
between 3 and 5 ft from the floor. A sling instrument should be used for
extreme accuracy. Thermocouples or resistance thermometers may also
be used for room temperature measurements, an advantage being that the
operator can read temperatures from outside the room if desired, and thus
eliminate the errors which might be caused by his presence close to the
temperature measuring device.
For measuring duct temperatures a duct thermometer should be used,
with the bulb extending into the duct at least 6 in. When the thermo-
meter is to be permanently located in the duct, a pipe flange or nipple
should be used to receive the threaded portion of the thermometer stem.
When the thermometer is not to be permanently located, a cork or rubber
stopper may be placed around the stem to prevent errors from air leakage.
Readings should be taken at various locations in a duct so due con-
sideration may be given to temperature stratification. Other forms of
temperature measuring devices may be used, but the active part must be
at least 6 inches from the duct wall.
Recording thermometers may be used for testing, and for making
continuous records of operation. Care should be taken, however, to
insure that time lag due to heavy measuring elements is kept to a mini-
mum, so that the recorders will properly follow temperature fluctuations.
Thermocouples made of fine wire will show less time lag than will many
mercury bulb thermometers.
677
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
MEASUREMENT OF AIR MOVEMENT
The quantity, velocity and pressure of air moved by a fan or flowing
through a duct or grille may be determined by various methods. The
instruments in common use are the Pitot tube, anemometer, direct
reading velocity meter, and Kata-thermometer, the latter being suitable
for low air velocities and being commonly used for measurements at
points where the air is not confined in a duct. The use of calibrated
nozzles, orifice plates, and Venturi meters are recognized methods, which,
however, have little application in connection with ventilation practice.
Pitot Tube
This usually consists of two tubes, one within the other, which when
properly held in the air stream will register the total or impact pressure
and the static pressure, respectively. If these tubes are connected to
opposite sides of a water column, or other type of manometer, the recorded
pressure will be the differential or velocity pressure. Volume measure-
ments may thus be made in a duct of known area. Pitot tube measure-
ments are preferably used for air velocities exceeding 20 fps. Volumetric
determinations from Pitot tube readings should take into account the
barometric pressure and the temperature and humidity of the air measured.
In general no accurate velocity pressure readings can be taken when the
flow of air in ducts is turbulent. To insure accuracy a straight section of
duct from 5 to 10 times its own diameter is desirable in order to straighten
out the air currents. If it is necessary to take Pitot tube readings in
shorter sections of straight duct, the results must be considered subject
to some doubt and checked accordingly. For accurate work it is neces-
sary to make a traverse of the duct, dividing its cross section into a
number of imaginary equal areas and taking a reading in the center of
each, the average^of the velocities corresponding to these pressures giving
the true velocity in the duct.
Anemometer
This instrument is delicate, and requires frequent calibration when
accuracy is desired. The vanes of the instrument should never be
touched and it should never be held in air having a velocity greater than
that for which it is calibrated. Readings taken directly in a fan inlet or
discharge are likely to harm the instrument because of excessive velocities.
In duct measurements the same procedure is followed as for the Pitot
tube. The anemometer usually reads directly in linear feet. To obtain
the velocity in feet per minute, the reading must be divided by the
elapsed time in minutes.
The following procedure for obtaining anemometer readings is based
on research conducted at Armour Institute of Technology in co5peration
with the A.S.H.V.E. Research Laboratory2.
Supply Grilles. The surface of the grille should be marked off into a
number of equal areas approximately 6 in. square. A 4-in. anemometer
'Measurement of Flow of Air through Registers and Grilles, by I/. E. Davies (A.S,H.V»B, TltANSACTtOHS^
Vol. 36, 1930, VoL 37, 1931, and A.S.H.V.E. Journal Section, Heating, Piping **& Air Conditioning, Sep-
tember, 1933). » «. K * r
678
CHAPTER 40 — TEST METHODS AND INSTRUMENTS
should be used and should be held at the center of each section in contact
with the grille (or as close as possible) for a period of time sufficient to
insure an average reading. In the case of supply grilles, the instrument
should always be held with the dial facing the operator. The average of
the corrected readings should then be used in the following formula to
obtain the flow in cubic feet per minute:
where
V — average of corrected anemometer readings, feet per minute.
A = gross area of grille, square feet.
a = net free area of grille, square feet.
p — percentage of free area of grille expressed as a decimal.
C «= a coefficient that varies with the velocity from grille and may vary slightly
with type of grille. For average use, with supply grilles, C can be taken
as 0.97 at velocities from 150 to 600 fpm, and as 1.00 at higher velocities.
Particular care should be exercised in the case of long, narrow grilles.
The nature of the approach sometimes results in there being a narrow
strip along the top or bottom of the grille through which no air will be
flowing. This may be detected by holding the anemometer completely
out of the air stream and then moving it slowly inward over the grille until
the vanes just start to move. The distance which the vanes extend over
the grille opening at this moment will indicate the width of the dead strip.
Only the remaining portion of the grille should be considered in making
the calculations for gross and free area.
Exhaust Grilles. The surface of the grille should be marked off and
readings taken in the same manner as with supply grilles, except that the
instrument should be held with the dial facing the grille, and in contact
with it. The traverse should be taken at a uniform rate, allowing suf-
ficient time in each space to minimize the percentage of error. In the case
of exhaust grilles it is found that the formula
tfm « KVA (2)
in which
V « average indicated velocity obtained by the anemometer traverse.
4 = gross area of grille, square feet.
j£ = coefficient determined by experiment. For average use, with exhaust grilles,
K may be taken as 0.8 for all usual velocities.
This formula is of advantage, especially with ornamental grilles, in
that the free area need not be measured.
The flow of air through registers and grilles is of considerable impor-
tance, being frequently the only convenient method of measuring the
volume of supply air to a room. While duct measurements, if available,
are more dependable, grille measurements provide a fairly accurate
method, if care is taken in the technique of using the anemometer.
Kata-Thermometer
The Kata-thermometer can be used to determine air velocities pro-
vided the walls and surrounding objects are at or near the room tern-
679
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
perature. Especially at low velocities it constitutes a useful instrument
for readily detecting drafts.
The instrument is essentially an alcohol thermometer with a bulb
approximately 5^ in. in diameter and J^ in. long with a stem 8 in. long
reading from 100 F to 95 F, graduated to tenths of a degree. To take
readings the bulb is heated in water until the alcohol expands and rises
into a top reservoir. The time in seconds required for the liquid to
fall from 100 F to 95 F is recorded with a stop watch and this time is a
measure of the rate of cooling.
The dry Kata loses its heat by radiation and by convection so for
constant velocities the time of cooling is a function of the dry-bulb tem-
perature of the surrounding air. The wet Kata, which has a cloth covering
fitted snugly around its bulb, loses heat by radiation, convection, and
evaporation, and for constant velocities its rate of cooling is a function of
the wet-bulb temperature of the air irrespective of the dry-bulb tem-
perature or relative humidity. It does not follow, however, that the
difference in rate of cooling of the dry and the wet Kata is caused by
evaporation. A change in the wet-bulb temperature produces a change in
the surface temperature of the wet Kata which in turn affects the heat
lost by radiation and by convection.
Several precautions should be taken to obtain the best results with this
instrument:
1. To obtain velocity readings use the dry Kata since the error in timing is reduced.
2. The instrument should be heated and allowed to cool two or three times before
recording the final time of cooling. The first reading is not reliable.
3. All traces of moisture must be removed from the dry Kata before timing to eli-
minate error introduced by evaporation.
4. Use only the formula applying to a particular instrument. Each Kata receives an
individual calibration.
HUMIDITY MEASUREMENT
The sling psychrometer is the recognized standard instrument for
determining humidities. In order to obtain accurate readings considerable
skill is required on the part of the operator. The wicking and water must
be clean and the temperature of the water should be slightly above the
wet-bulb temperature of the surrounding air. The psychrometer should
be swung rapidly and several and frequent observations should be made
to see that the wet-bulb temperature has become stationary before the
final reading is noted. Care should be taken that the wet-bulb has
reached a minimum temperature, but the wick must still be moist.
Standard psychrometric tables should be used.
In making wet-bulb measurements below 32 F the same procedure is
followed as above 32 F. The water is liquid at the start, but as the sling
is operated it will freeze rapidly enough so that in quickly giving up the
latent heat of fusion, the indicated wet-bulb temperature may drop
below the actual wet-bulb temperature. After the liquid on the bulb has
become thoroughly frozen the wet-bulb temperature will rise to normal.
A very thin film of ice is more desirable than a thick film. Care must be
taken to read the temperatures in the region below 32 F accurately
because the spread between the wet- and dry-bulb is small,
680
CHAPTER 40 — TEST METHODS AND INSTRUMENTS
In taking humidity readings in ducts it is usually impracticable to use
a sling psychrometer. For this work the stationary hygrodeik arranged
for bolting on to the side of the duct, with two bulbs extending into the
duct, will be found very convenient. Owing to the velocity of the air
passing over the bulbs within the duct an accurate reading will be secured,
corresponding to that given by the sling psychrometer.
Various forms of humidity recorders are available, some merely re-
cording wet- and dry-bulb temperatures, and others recording relative
humidity directly. Any form of wet- and dry-bulb device must have
sufficient air velocity over the thermometer bulbs to insure accurate
readings ; this velocity should be secured by a fan if the air is not itself in
motion, as in a duct. For extremely low humidities, or for humidity
measurements above 212 F, a thermal conductivity method is available3.
CARBON DIOXIDE DETERMINATION4
At ordinary concentrations carbon dioxide is not harmful. The amount
of carbon dioxide in the air is a convenient index of the rate of air supply,
and of the distribution of the air within rooms. Unequal carbon dioxide
concentrations in parts of a room indicate improper air distribution.
The Petterson-Palmquist apparatus has been generally accepted as the
standard device for the determination of carbon dioxide in air investiga-
tions. The principle involved is the measurement of a given volume of
air, the absorption of the contained carbon dioxide in a caustic potash
solution, and the remeasurement of the volume of air at the original
pressure in a finely graduated capillary tube, the difference in volume
representing the absorbed carbon dioxide. (See Report of Committee on
Standard Methods for Examination of Air, American Public Health Asso-
ciation, Vol. 7, No. 1; American Journal of Public Health, Jan., 1917.)
Where field conditions are such that this apparatus may not be con-
veniently used, as in street cars, air samples may be collected in clean
bottles having mercury-sealed rubber stoppers, and these may be sub-
jected to laboratory analysis.
DUST DETERMINATION
Many laboratory methods have been developed to measure the dust in
the air. These involve the collection of dust on sticky plates, on filter
paper, in water, on porous crucibles, or by electric precipitation, and the
subsequent determination of the amount of dust by microscopic counting,
weighing, or titration. While there is no standard method, the Hill
dust counter, using a microscope, the impinger6, using chemical changes
in water, and the Lewis sampling tube6, involving the analytical weighing
of a porous crucible, are accepted. All test results should be accompanied
by the name of the instrument used as great variation in counts with the
'"Gas Analysis by Measurement of Thermal Conductivity," H. A. Daynes, Cambridge Press, 1933.
*See A.S.H.V.E. research paper entitled Indices of Air Change and Air Distribution, by F. C. Houghten
and J. L, Blackshaw (A.S,H.V,E. Journal Section, Keating, Piping and Air Conditioning, June, 1933).
'Public Health Bulletin, No. 144, 1925, U. S. Public Health Service.
•Testing and Rating of Air Cleaning Devices Ueed for General Ventilation Work, by Samuel R. Lewis
(A.S.H.V.E. Journal Section^ Heating, Piping and Air Conditioning, May, 1933),
681
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
different instruments will be obtained. The AMERICAN SOCIETY OF
HEATING AND VENTILATING ENGINEERS has developed a code7 for the
testing and rating of air cleaning devices used in general ventilation work.
FLUE CAS ANALYSIS
The analysis of flue gases by chemical means is made with the Orsat
apparatus. A solution of KOH is used to absorb the C02. Free oxygen is
absorbed by a mixture of pyrogallic acid and KOH. The solution for
absorbing the CO is cuprous chloride. The apparatus consists of a
burette surrounded by a water jacket, to receive and measure the volume
of gas. The burette is connected by a manifold of glass to pipettes con-
taining liquids for absorbing CO^ 0% and CO.
Various forms of automatic indicating and recording gas analysis
devices are available, operating on either chemical or physical principles.
Such devices are convenient for plant operation.
MEASUREMENT OF SMOKE DENSITY
Relative smoke density is usually measured by comparison with the
Ringelmann Chart (Fig. 1). In making observations of the smoke issuing
from a chimney, four cards ruled like those in Fig. 1, together with a card
printed in solid black and another left entirely white, are placed in a
horizontal row and hung at a point 50 ft from the observer and con-
veniently in line with the chimney. At this distance, the lines become
invisible, and the cards appear to be of different shades of gray, ranging
from very light gray to almost black. The observer glances from the
smoke coming from the chimney to the cards, which are numbered from
0 to 5, determines which card most nearly corresponds with the color of
the smoke, and makes a record accordingly, noting the time. Observa-
tions are made continuously during one minute, and the estimated average
density during that minute recorded. The average of all the records
made during a boiler test is taken as the average figure for the smoke
density during the test, and the entire record is plotted on cross-section
paper in order to show how the smoke varied in density from time to time*
Smoke Recorders
Smoke recorders are available which give a much more accurate in-
dication of the amount of smoke being produced than does the Ringel-
mann Chart. Although most of these Instruments are in the process of
development, they constitute a satisfactory tool in the control of smoke
emission. They all depend upon projecting a beam of light through the
smoke flue or through a separate compartment from which a sample of the
flue gas is drawn continuously. The light of the beam which passes
through without being absorbed by the smoke is measured to determine
the smoke density. Most of these instruments make use of a photo-
electric cell or a thermopile to measure the relative amount of light which
has not been absorbed. Standard electrical instruments serve for in-
dicating or recording.
'See A.S.H.V.E. Standard Code for Testing and Rating Air Cleaning Devices Used in General Ventila-
tion Work, edition of July, 1934,
682
CHAPTER 40 — TEST METHODS AND INSTRUMENTS
MEASUREMENT OF RATE OF HEAT TRANSMISSION
The standard methods of testing built-up wall sections are by means of
the guarded hot-box* and the guarded hot-plate*. The Nicholls heat-flow
meter9 may be used for testing actual walls of buildings.
It would be obviously impossible to determine the air-to-air heat trans-
mission coefficients of every type of wall construction in use with the
heat-flow meter, the guarded hot-box or the guarded hot-plate on account
of the great amount of time involved. Hence, the method of computing
the coefficients from the fundamental constants must be resorted to in
most cases. The guarded hot-plate is used to determine the fundamental
FlG. 1. RlNGELMANN SMOKE CHART
constants. The heat-flow meter, guarded hot-box and guarded hot-plate
tests can be used to good advantage in checking the accuracy of the
computed values.
If the hot-box or hot-plate methods are used, tests are usually run under
still air conditions, which means there is no wind movement over the
surfaces of the wall during the test. In the hot-plate method of test the
inside surface coefficient is eliminated by the plate's being in direct contact
with the wall. In practice, some wind movement over the exterior surface
of the wall should always be allowed for; hence, still-air coefficients cannot
be used over the outside of the building during the heating season.
Moreover, still-air transmission coefficients cannot be corrected to provide
for moving-air conditions by applying a single constant factor. Computed
coefficients of transmission for various types of construction are given
in Chapter 5.
EUPATHEOSCOPE
The eupatheoscope affords a means of evaluating the combined effect of
radiation and convection in a given environment in terms of a standard
environment and in some terms related to human comfort. See Chapter
38.
•See Standard Code for Heat Transmission through Walls (A.S.H.V.E. TRANSACTIONS, Vol. 34, 1928>
and Report of the Committee on Heat Transmission, National Research Council.
•See Measuring Heat Transmission in Building Structures and a Heat Transmission Meter, by P..
Nlcholls (A,S,H,VJ& TRANSACTIONS, Vol. 30, 192*7,
683
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
PROBLEMS IX PRACTICE
1 • The hand on a pressure gage attached to a steam line indicates a pressure
of 15 Ib per square inch and the barometric pressure is 14.7 Ib per square inch.
What is the absolute pressure, in pounds per square inch, being exerted by
the steam?
The absolute pressure exerted by the steam in the pipe is equal to the pressure indicated
by the gage plus that exerted by the atmosphere.
Total pressure = 15 -f 14.7 == 29.7 Ib per square inch.
2 • Outline the procedure to be followed in taking room temperatures.
In taking room temperatures, a standard mercury thermometer should be used, with
care taken that no part of the observer's body is nearer than 10 in. to the thermometer
bulb. The thermometer should be held at least 5 ft away from any window, door or
opening; it should be at least 12 in. away from any wall, and should be between 3 and 5
ft from the floor.
3 • What advantages other than its sensitiveness, has the U-tube draft gage or
manometer for measurement of low pressures?
Inherent accuracy without calibration and low cost of the essential parts, which are
glass tubing and an ordinary scale.
4 • Are thermocouples as accurate as mercury thermometers?
Within the range which can be measured with both instruments (below 1000 F) either
one may be made as sensitive as the service requires. The accuracy of a thermocouple
temperature measurement depends chiefly on :
1. An accurate calibration of the wire.
2. The sensitiveness of the electrical instrument.
3. Accurate cold-junction control.
4. Proper placement of the sensitive junction.
5 • Is room temperature accurately measured by the ordinary wall thermo-
meter?
No, Wall thermometer measurements may be several degrees in error as compared with
an observation properly made in the zone of occupancy,
6 • When an anemometer is used for measuring the air discharged from a
grille or register, does it read the velocity through the gross face area or the
velocity through the net free area?
Neither. If either of these velocities is required, it should be calculated by means of
Equation 1.
7 • Do common errors made in humidity determination produce a result that
is too high or too low?
A higher relative humidity than the true value is likely to be found, either because there
is insufficient velocity over the wet-bulb or because the reading is not taken at the right
time.
8 • What is the purpose of the carbon dioxide determination?
It is an index of the adequacy of fresh air supply and also an indicator of air distribution.
684
Chapter 41
TERMINOLOGY
Glossary of Physical and Heating and Ventilating Terms Used
in the Text, Standard Abbreviations, Conversion Equations,
Drafting Symbols, A.S.H.V.E. Codes
Absolute Humidity: See Humidity.
Absolute Pressure: The sum, at any particular time, of the gage
pressure and the atmospheric pressure.
Absolute Temperature: The temperature of a substance measured
above absolute zero.
Absolute Zero: The temperature ( — 459.6 F) at which the molecular
motion of a substance theoretically ceases. This is the temperature at
which the substance theoretically contains no heat energy.
Acceleration: The rate of change of velocity. In the fps system
this is expressed in units of one foot per second per second.
Acceleration Due to Gravity : The rate of gain in velocity of a freely
falling body. In the fps system this is 32.174 feet per second per second.
Adiabatic: An adjective pertaining to or designating variations in
volume or pressure not accompanied by gain or loss of heat. When a
substance undergoes adiabatic expansion, since it does not receive heat
from without, the work which it does is at the expense of its internal
energy, and therefore its temperature falls; similarly, when it is adia-
batically compressed its temperature rises.
Adsorption: The adhesion of the molecules of gases or dissolved sub-
stances to the surfaces of solid bodies, resulting in a concentration of the
gas or solution at the place of contact,
Air Cleaner: A device designed for the purpose of removing air-borne
impurities such as dusts, fumes, and smokes. (Air cleaners include air
washers and air filters,)
Air Conditioning: The simultaneous control of all or at least the first
three of those factors affecting both the physical and chemical conditions
of the atmosphere within any structure. These factors include tempera-
ture, humidity, motion, distribution, dust, bacteria, odors, toxic gases,
and ionization, most of which affect in greater or lesser degree human
health or comfort.
Air Infiltration : The inleakage of air through cracks and crevices,
and through doors, windows and other openings, caused by wind pressure
or temperature difference.
685
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Air Washer: An enclosure in which air is forced through a spray of
water in order to cleanse, humidify, or dehumidify the air.
Anemometer: An instrument for measuring the velocity of moving
air,
Atmospheric Pressure: The pressure exerted by the atmosphere in
all directions, as indicated by a barometer. Standard atmospheric pressure
is considered to be 14.7 Ib per square inch, which is equivalent to 29.92 in.
of mercury.
Baffle: A plate or wall for deflecting gases or fluids.
Blast: This word was formerly used to denote forced air circulation,
particularly in connection with central fan systems using steam or hot
water as the heating medium. As applied in this sense, the word blast
is now obsolete.
Boiler: A closed vessel in which steam is generated or in which water is
heated.
Boiler Heating Surface: That portion of the surface of the heat-
transfer apparatus in contact with the fluid being heated on one side and
the gas or refractory being cooled on the other, in which the fluid being
heated forms part of the circulating system ; this surface shall be measured
on the side receiving heat. This includes the boiler, water walls, water
screens, and water floor. (A.S.M.E. Power Test Codes, Series 1929.)
Boiler Horsepower: The equivalent evaporation of 34.5 Ib of water
per hour from and at 212 F. This is equal to a heat output of 970.2 X
34.5 = 33,471.9 Btu per hour.
British Thermal Unit: The mean British thermal unit is - of the
heat required to raise the temperature of 1 Ib of water from 32 F to 212 F.
It is substantially equal to the quantity of heat required to raise 1 Ib of
water from 63 F to 64 F. One Btu = ^-5" kwhn
By-pass : A pipe or duct, usually controlled by valve or damper, for
short-circuiting fluid flow.
Calorie: The mean calorie is -r-nn °f ^e heat required to raise the
J.UU
temperature of 1 gram of water from Zero C to 100 C. It is substantially
equal to the quantity of heat required to raise one gram of water from
14.5 C to 15.5 C.
Central Fan System: A mechanical indirect system of heating,
ventilating, or air conditioning, in which the air is treated or handled by
equipment located outside the rooms served, usually at a central location,
and is conveyed to and from the rooms by means of a fan and a system of
distribution ducts. See Chapters 9 and 22.
Chimney Effect: The tendency in a duct or other vertical air passage
for air to rise when heated, owing to its decrease in density.
Coefficient of Transmission: The amount of heat (Btu) transmitted
from air to air in one hour per square foot of the wall, floor, roof or ceiling
for a difference in temperature of 1 F between the air on the inside and that
on the outside of the wall, floor, roof or ceiling.
686
CHAPTER 41 — TERMINOLOGY
Column Radiator: A type of direct radiator. This radiator has not
been listed by manufacturers since 1926.
Comfort Line: The effective temperature at which the largest per-
centage of adults feel comfortable.
Comfort Zone' (Average): The range of effective temperatures over
which the majority (50 per cent or more) of adults feel comfortable.
Comfort Zone (Extreme): The range of effective temperatures over which
one or more adults feel comfortable. (See Chapter 2.)
Concealed Radiator : See Convector.
Conductance: The amount of heat (Btu) transmitted from surface
to surface in one hour through one square foot of a material or construc-
tion, whatever its thickness, when the temperature difference is 1 F
between the two surfaces.
Conduction; The transmission of heat through and by means of
matter unaccompanied by any obvious motion of the matter.
Conductivity: The amount of heat (Btu) transmitted in one hour
through one square foot of a homogeneous material 1 in. thick for a
difference in temperature of 1 F between the two surfaces of the material.
Conductor (heat): A material capable of readily conducting heat.
The opposite of an insulator or insulation.
Constant Relative Humidity Line: Any line on the psychrometric
chart representing a series of conditions which may be evaluated by one
percentage of relative humidity; there are also constant dry-bulb lines,
wet-bulb lines, effective temperature lines, vapor pressure lines, and
lines showing other physical properties of air mixed with water vapor.
Control: Any manual or automatic device for the regulation of a
machine to keep it at normal operation. If .automatic, it is considered
that the device is motivated by variations in temperature, pressure,
time, light, or other influences.
Convection: The transmission of heat by the circulation of a liquid
or a gas such as air. Convection may be natural or forced.
Convector: A concealed radiator. A heating unit and an enclosure
or shield located either within, adjacent to, or exterior -to the room or
space to be heated, but transferring heat to the room or space mainly by
the process of convection. If the heating unit is located exterior to the
room or space to be heated, the heat is transferred through one or more
ducts or pipes; see Chapter 30.
Corrosive: Having the power to wear away or gradually change the
texture or substance of a material.
Decibel: The standard unit for noise or sound intensity. One decibel
is equal to ten times the logarithm to the base e of the ratio of the sound
intensities.
Degree-Day: "A unit, based upon temperature difference and time,
used in specifying the nominal heating load in winter. For any one day
there exist as many degree-days as there are degrees Fahrenheit dif-
ference in temperature between the average outside air temperature,
taken over a 24-hour period, and a temperature of 65 F.
687
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Dehumidify : To remove water vapor from the atmosphere; to
remove water vapor or moisture from any material.
Density: The weight of a unit volume, expressed in pounds per cubic
W
foot, p (rho) = -~r.
Dew-Point Temperature : The temperature corresponding to satura-
tion (100 per cent relative humidity) for a given moisture content.
Diffuser: A vaned device placed at an air supply opening to direct the
air flow.
Direct-Indirect Heating Unit: A heating unit located in the room
or space to be heated and partially enclosed, the enclosed portion being
used to heat air which enters from outside the room.
Direct Radiator : Same as radiator.
Direct-Return System (Hot water): A hot water system in which the
water, after it has passed through a heating unit, is returned to the boiler
along a direct path so that the total distance traveled by the water is the
shortest feasible, and so that there are considerable differences in the
lengths of the several circuits composing the system.
Down-Feed One-Pipe Riser (Steam): A pipe which carries steam
downward to the heating units and into which the condensation from the
heating units drains.
Down-Feed System (Steam): A steam heating system in which the
supply mains are above the level of the heating units which they serve.
Draft Head (Side Outlet Enclosure) : The height of a gravity convector
between the bottom of the heating unit and the bottom of the air outlet
opening.
Draft Head (Top Outlet Enclosure): The height of a gravity convector
between the bottom of the heating unit and the top of the enclosure.
Dry Air: Air with which no water vapor is mixed. This term is used
comparatively, since in nature there is always some water vapor included
in air, and such water vapor, being a gas, is dry.
Dry -Bulb Temperature: The temperature of the air indicated by
any type of thermometer not affected by the water vapor content or
relative humidity of the air.
Dry Return: A return pipe in a steam heating system which carries
both water of condensation and air. See wet return.
Dust: Solid material in a finely divided state, the particles of which
are large and heavy enough to fall with increasing velocity, due to gravity
in still air. For instance, particles of fine sand or grit, the average
diameter of which is approximately 0.01 centimeter, such as are blown
on a windy day, may be called dust.
Dynamic Head or Pressure: The total or impact pressure. This is
the sum of the radial pressure and the velocity pressure at the point of
measurement.
Effective Temperature: An arbitrary index of the degree of warmth
or cold felt by the human body in response to temperature, humidity,
and movement of the air. Effective temperature is a composite index
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CHAPTER 41 — TERMINOLOGY
which combines the readings of temperature, humidity, and air motion
into a single value. The numerical value of the effective temperature
scale has been fixed by the temperature of saturated air which induces an
identical sensation of warmth.
Enthalpy: Total heat or thermal potential.
Entropy: The logarithmic probability of a state. It is the integra-
tion between two absolute temperatures of the quotient of the quantity
of heat divided by the absolute temperature at the condition at which the
temperature is taken. It is, therefore, a numeric which explains a dif-
ference in conditions between two points in a heat cycle.
Entropy, which can vary with temperature, volume, or pressure, is
constant during adiabatic expansion in a reversible cycle or during
isentropic expansion in an irreversible cycle. Entropy is a function of the
unavailable energy in any system.
Equivalent Evaporation: The amount of water a boiler would
evaporate, in pounds per hour, if it received feed water at 212 F and
vaporized it at the same temperature and atmospheric pressure.
Estimated Design Load: The load, stated in Btu per hour or equiv-
alent direct radiation, as estimated by the purchaser for the conditions of
inside and outside temperature for which the amount of installed radiation
was determined. It is the sum of the heat emission of the radiation to be
actually installed plus the allowance for the heat loss of the connecting
piping plus the heat requirement for any apparatus requiring heat con-
nected with the system. (A.S.H.V.E. Standard Code for Rating Steam
Heating Solid Fuel Hand-Fired Boilers— edition of April 1932.)
Estimated Maximum Load: Construed to mean the load stated in
Btu per hour or equivalent direct radiation that has been estimated by
the purchaser to be the greatest or maximum load that the boiler will be
called upon to carry. (A.S.H.V.E. Standard Code for Rating Steam
Heating Solid Fuel Hand-Fired Boilers— edition of April 1932.)
Extended Heating Surface: See Heating Surface.
Extended Surface Heating Unit: A heating unit having a relatively
large amount of extended surface which may be integral with the core
containing the heating medium or assembled over such a core, making
good thermal contact by pressure or by being soldered to the core or by
both pressure and soldering. An extended surface heating unit is usually
placed within an enclosure and therefore functions as a convector.
Fan Furnace System: See Warm Air Heating System.
Force: The action on a body which tends to change its relative con-
WV
dition as to rest or motion. F = — -.
Fumes: Particles of solid matter resulting from such chemical pro-
cesses as combustion, explosion, and distillation, ranging from 0.1 to 1.0
micron in size.
Furnace: That part of a boiler or warm air heating plant in which
combustion takes place. Also, a fire-pot.
Furnace Volume (Mai): The total furnace volume for horizontal-
return tubular boilers and water-tube boilers is the cubical contents of the
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
furnace between the grate and the first plane of entry into or between
tubes. It therefore includes the volume behind the bridge wall as^in
ordinary horizontal -return tubular boiler settings, unless manifestly in-
effective (i.e., no gas flow taking place through it), as in the case of waste-
heat boilers with auxiliary coal furnaces, where one part of the furnace is
out of action when the other is being used. For Scotch or other internally
fired boilers it is the cubical contents of the furnace, flues and combustion
chamber, up to the plane of first entry into the tubes. (A.S.M.E. Power
Test Codes, Series 1929.)
Gage Pressure: Pressure measured from atmospheric pressure as a
base. Gage pressure may be indicated by a manometer which has one leg
connected to the pressure source and the other exposed to atmospheric
pressure.
Grate Area : The area of the grate surface, measured in square feet,
to be used in estimating the rate of burning fuel. This area is construed
to mean the area measured in the plane of the top surface of the grate,
except that with special furnaces, such as those having magazine feed, or
special shapes, the grate area shall be the mean area of the active part of
the fuel bed taken perpendicular to the path of the gases through it.
For furnaces having a secondary grate, such as those in double-grate
down-draft boilers, the effective area shall be taken as the area of the
upper grate plus one-eighth of the area of the lower grate, both areas
being estimated as defined above. (A.S.H.V.E. Standard and Short
Form Heat Balance Codes for Testing Low-Pressure Steam Heating
Solid Fuel Boilers.)
Gravity Warm Air Heating System: See Warm Air Heating System.
Grille: A perforated covering for an air inlet or outlet usually made
of wire screen, pressed steel, cast-iron or plaster. Grilles may be plain
or ornamental.
Heat: A form of energy generated by the transformation^ some other
form of energy, as by combustion, chemical action, or friction. Accord-
ing to the molecular theory, heat consists of the kinetic and potential
energy of the .molecules of a substance. The addition of heat energy to a
body increases the temperature or the kinetic energy of motion of its
molecules (sensible heat} or increases their potential energy of position but
does not increase the temperature, as when melting or boiling occurs
(latent heat).
Heat Capacity : The amount of heat (Btu or. calories) required to
raise the temperature of a body of any mass and variety of parts one
degree (Fahrenheit or centigrade). This will depend on the masses and
specific heats of the various parts of the body.
Therefore
$ » m\ Si -f- *»z $1 4- Wa 5B . . * . etc.
where
S is the heat capacity and m^ m* #*», and s\, 5j, s\ stand for the masses and cor-
responding specific heats of the parts, respectively.
Heating Medium: A substance such as water, steam, air, electricity
690
CHAPTER 41 — TERMINOLOGY
or furnace gas used to convey heat from the boiler, furnace or other source
of heat or energy to the heating unit from which the heat is dissipated.
Heating Surface: The exterior surface of a heating unit. Extended
heating surface (or extended surface): Heating surface having air on both
sides and heated by conduction from the prime surface. Prime Surface:
Heating surface having the heating medium on one side and air (or
extended surface) on the other. (See also Boiler Heating Surface.)
Heat of the Liquid : The sensible heat of a mass of liquid above an
arbitrary zero.
Horsepower : A unit to indicate the time rate of doing work equal to
550 ft-lb per second or 33,000 ft-lb per minute. (One horsepower =
745.8 watts. In practice this is considered 746 watts.)
Hot Water Heating System: A heating system in which water is
used as the medium by which heat is carried through pipes from the boiler
to the heating units.
Humidify: To add water vapor to the atmosphere; to add water
vapor or moisture to any material.
Humidity: The water vapor mixed with dry air in the atmosphere.
Absolute humidity refers to the weight of water vapor per unit volume of
space occupied, expressed in grains or pounds per cubic foot. Specific
humidity refers to the weight of water vapor in pounds carried by one Ib of
dry air. Relative humidity is a ratio, usually expressed in per cent, used to
indicate the degree of saturation existing in any given space resulting
from the water vapor present in that space. Relative humidity is either
the ratio of the actual partial pressure of the water vapor in the air to the
saturation pressure at the dry-bulb temperature, or the ratio of the actual
density of the vapor to the density of saturated vapor at the dry-bulb
temperature. The presence of air or other gases in the same space at the
same time has nothing to do with the relative humidity of the space.
Htimidis tat : A regulatory device, actuated by changes in humidity,
used for the control of humidity.
Hygrostat: Same as humidistat.
Inch of Water: A measure of pressure which refers to the difference
in the heights of the legs of a water filled manometer.
Insulation (heat): A material having a relatively high heat-resistance
per unit of thickness.
Isobaric: An adjective used to indicate a change taking place at con-
stant pressure.
Isothermal: An adjective used to indicate a change taking place at
constant temperature.
Latent Heat : See Heat.
Laws of Thermodynamics : The first law states that the total energy
of an isolated system remains constant and cannot be increased or dimini-
shed by any physical process whatever. The second law states that no
change in a system of bodies that takes place of itself can increase the
available energy of a system.
Manometer: An instrument for measuring pressures; essentially a
U-tube partially filled with a liquid, usually water, mercury, or a light
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
oil, so the amount of displacement of the liquid indicates the pressure
Toeing exerted on the instrument.
Mass: The quantity of matter, in pounds, to which the unit of force
(one pound) will give an acceleration of one foot per second per second.
W
m = — -.
g
Mb, Mbh1: Symbols which represent, respectively, 1000 Btu and
1000 Btu per hour.
Mechanical Equivalent of Heat: The mechanical energy necessary
to produce 1 Btu of heat energy. J = 777.5 ft-lb.
Micron: A unit of length, the thousandth part of one millimeter or
the millionth of a meter.
Mol: The unit of weight for gases. It is defined as m Ib where m
denotes the molecular weight of a gas. For any gas the volume of
1 mol at 32 F and standard atmospheric pressure is 358.65 cu ft and the
weight of a cubic foot is 0.002788 m Ib.
Neutral Zone: The level within a room or building at which the
pressure is exactly equal to the outside barometric pressure.
One-Pipe Supply Riser (steam): A pipe which carries steam upward
to a heating unit and which also carries the condensation from the heating
unit in a direction opposite to the steam flow.
One-Pipe System (hot water] : A hot water system in which the water
flows through more than one heating unit before it returns to the boiler ;
consequently, the heating units farthest from the boiler are supplied
with cooler water than those near the boiler in the same circuit.
One-Pipe System (steam) : A steam heating system consisting of a
main circuit in which the steam and condensate flow in the same pipe,
usually in opposite directions. Ordinarily to each heating unit there is
but one connection which must serve as both the supply and the return,
although separate supply and return connections may be used.
Overhead System: Any steam or hot water system in which the
supply main is above the heating units. With a steam system the return
must be below the heating units; with a water system, the return may
be above the heating units.
Panel Radiator: A heating unit placed on or flush with a flat wall
•surface and intended to function essentially as a radiator*
Panel Warming : A method of heating involving the installation of
the heating units (pipe coils) within the wall, floor or ceiling of the room,
so that the heating process takes place mainly by radiation from the wall,
floor or ceiling surfaces to the objects in the room.
Plenum Chamber: An air compartment maintained under pressure
and connected to one or more distributing ducts,
Potentiometer: An instrument for measuring or comparing small
electromotive forces.
Power: The rate of performing work, expressed in units of horse-
power, one of which is equal to 550 ft-lb of work per second, or 33,000 ft-lb
per minute.
Tfas* symbols wert approved by the A,S.H,V.E,» June, 1933.
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CHAPTER 41 — TERMINOLOGY
Prime Surface : See Heating Surface.
Psychrometer: An instrument for ascertaining the humidity or
hygrometric state of the atmosphere. Psychrometric: Pertaining to
psychrometry or the state of the atmosphere as to moisture. Psychro-
metry: The branch of physics that treats of the measurement of degree of
moisture, especially the moisture mixed with the air.
Pyrometer: An instrument for measuring high temperatures.
Radiation: The transmission of heat through space by wave motion.
Radiator: A heating unit exposed to view within the room or space to
be heated. A radiator transfers heat by radiation to objects "it can see"
and by conduction to the surrounding air which in turn is circulated by
natural convection ; a so-called radiator is also a convector but the single
term radiator has been established by long usage. Concealed Radiator:
See Convector.
Recessed Radiator: A heating unit set back into a wall recess but
not enclosed.
Refrigerant: A substance which produces a refrigerating effect by its-
absorption of heat while expanding or vaporizing.
Register : A grille with a built-in muitiblade damper or shutter.
Relative Humidity: See Humidity: see also discussion of relative-
humidity in Chapter 1.
Return Mains : The pipes which return the heating medium from the
heating units to the source of heat supply.
Reversed-Return System (hot water): A hot water heating system*
in which the water from several heating units is returned along paths
arranged so that all circuits composing the system or composing a major-
subdivision of the system are practically of equal length.
Roof Ventilator: A device placed on the roof of a building to permit
egress of air.
Saturated Air: Air containing as much water vapor as it can hold
without any condensing out; in saturated air, the partial pressure of the
water vapor is equal to the vapor pressure of water at the- existing tem-
perature.
Sensible Heat: See Heat.
Smoke: Carbon or soot particles less than 0.1 micron in^size which
result from the incomplete combustion of carbonaceous materials such as
coal, oil, tar, and tobacco.
Smokeless Arch: An inverted baffle placed in an up-draft furnace
toward the rear to aid in mixing the gases of combustion and thereby to
reduce the smoke produced.
Specific Gravity: The ratio of the weight of a body to the weight of
an equal volume of water at some standard temperature, usually 39.2 F.
Specific Heat: The quantity of heat, expressed in Btu, required to
raise the temperature of 1 Ib of a substance 1 F.
Specific Volume: The volume, expressed in cu ft, of one pound of
t 1 v
a substance, v = — • «= ^7.
p W
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Split System: A system in which the heating and ventilating are
accomplished by means of radiators or convectors supplemented by
mechanical circulation of air (heated or unheated) from a central point.
Square Foot of Heating Surface (equivalent): Equivalent direct
radiation (EDR). By definition, that amount of heating surface which
will give off 240 Btu per hour. The equivalent square feet of heating
surface may have no direct relation to the actual surface area,
Stack Height: The height of a gravity con vector between the bottom
of the heating unit and the top of the outlet opening.
Standard Air: As defined by A.S.H.V.E. codes, standard air is air
weighing 0.07488 Ib per cubic foot, which is air at 68 F dry-bulb and
50 per cent relative humidity with a barometric pressure of 29.92 in. of
mercury. (Most engineering tables and formulae involving the weight
of air are based on air weighing 0.07495 Ib per cubic foot, which is dry air
at 70 F dry-bulb with a barometric pressure of 29.92 in. of mercury. The
error involved in disregarding the difference between the above two
weights is very slight and in most instances may be neglected.)
Static Pressure: The compressive pressure existing in a fluid. It is
a measure of the potential energy of the fluid.
Steam: Steam is water vapor which exists in the vaporous condition
because sufficient heat has been added to the water to supply the latent
heat of evaporation and change the liquid into vapor. Steam in contact
with the water from which it has been generated may be dry saturated
steam or wet saturated steam. The latter contains more or less actual
water in the form of mist. If steam is heated, and the pressure main-
tained the same as when it was vaporized, its temperature will increase
and it will become superheated.
Steam Heating System : A heating system in which heat is trans-
ferred from the boiler or other source of steam to the heating units by
means of steam at, above, or below atmospheric pressure.
Steam Trap : A device for allowing the passage of condensate and
preventing the passage of steam, or for allowing the passage of air as
well as condensate.
Superheated Steam: See Steam.
Supply Mains (steam): The pipes through which the steam flows
from the boiler or source of supply to the run-outs and risers leading to the
heating units.
Surface Conductance: The amount of heat (Btu) transmitted by
radiation, conduction, and convection from a surface to the air or liquid
surrounding it, or vice versa, in one hour per square foot of the surface for
a difference in temperature of 1 deg between the surface and the sur-
rounding air or liquid,
Synthetic Air Chart; A chart for evaluating the air conditions
maintained in a room.
Thermal Resistance: The reciprocal of conductance.
Thermal Resistivity: The reciprocal of conductivity. *
Thermodynamics: The science which treats of the mechanical
actions or relations of heat.
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CHAPTER 41 — TERMINOLOGY
Thermostat: An instrument which responds to changes in tempera-
ture and which directly or indirectly controls the source of heat supply.
Ton of Refrigeration : The extraction of 12,000 Btu per hour.
Ton Day of Refrigeration : The heat removed by a ton of refriger-
ation operating for one day; 288,000 Btu.
Total Heat: A thermodynamic quantity, variously called heat con-
tent, thermal potential, enthalpy. It is the heat required per unit mass
(Btu per Ib) to raise a given substance to a given point from an arbitrary
datum point. It is the sum of the heat of the liquid, the latent heat,
and any miscellaneous heat which may be present.
Total Pressure: The sum of the static and velocity pressures in a
fluid. It is a measure of the total energy of the fluid.
Tube (or Tubular) Radiator: A cast-iron heating unit used as a
radiator and having small vertical tubes.
Two-Pipe System (steam or water): A heating system in which one
pipe is used for the supply of the heating medium to the heating unit and
another for the return of the heating medium to the source of heat
supply. The essential feature of a two-pipe system is that each heating
unit receives a direct supply of the heating medium which medium cannot
have served a preceding heating unit.
Underfeed Distribution System (hot water): A hot water heating
system in which the main flow pipe is below the heating units.
Underfeed Stoker: A stoker which feeds the coal underneath the fuel
bed.
Unit Air Conditioner: A piece of equipment designed to provide
simutaneous control of at least four of the seven functions " (page 201)
involved in summer and winter air conditioning. The apparatus is com-
pactly housed in a cabinet placed within or immediately adjacent to the
rooms served. The parts comprising a unit air conditioner are assembled
at the point of manufacture, and the performance of the assembly is the
responsibility of the manufacturer. See Chapter 12.
Unit Cooler: A cooling device, usually comprising an extended-
surface element and a motor-driven fan mounted integrally in a housing,
located within or adjacent to the room served. Generally no ducts are
attached to inlet or outlet. The refrigerant is brought to the unit from
an outside source, and the fan drives air over the cooling element.
Unit Heater: A heating device, usually comprising an extended-
surface element or a gas burner, mounted with a motor-driven fan in a
housing, located within or adjacent to the room served. Generally, no
ducts are attached to inlet or outlet, The fluid for heating is brought to
the unit from an outside source, and the fan drives air over the heating
element. Unit heaters are used primarily in industrial applications.
Unit Ventilating-Heater : A ventilating and heating device com-
prising a motor-driven fan, an extended-surface heating element and
usually a filter, mounted in a housing, located within or adjacent to the
room served. Outdoor air is obtained through a dampered direct con-
nection or a short duct from a nearby wall or window opening. Provision
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
for partial recirculation is usually made. If a humidifier is included, such
a filter-equipped device becomes a winter-type unit conditioner. Unit
ventilators are used primarily for offices, schools, and places of public
assembly.
Up-Feed System (steam): A steam heating system in which the
supply mains are below the level of the heating units which they serve.
Vacuum Heating System: A two-pipe steam heating system equip-
ped with the necessary accessory apparatus which will permit operating
the system below atmospheric pressure when desired.
Vapor: Any substance in the gaseous state.
Vapor Heating System: A steam heating system which operates
under pressures at or near atmospheric and which returns the condensa-
tion to the boiler or receiver by gravity. Vapor systems have thermo-
static traps or other means of resistance on the return ends of the heating
units for preventing steam from entering the return mains; they also have
a pressure-equalizing and air-eliminating device at the end of the dry
return. Direct Vent Vapor System: A vapor heating system with air
valves which do not permit re-entry of air.
Vapor Pressure: The equilibrium pressure exerted by a vapor in
contact with its liquid.
Velocity: The time rate of motion of a body in a fixed direction. In
the fps system it is expressed in units of one foot per second. V = ™.
Velocity Pressure: The pressure corresponding to the velocity of
flow. It is a measure of the kinetic energy of the fluid.
Ventilation: The process of supplying or removing air by natural or
mechanical means, to or from any space. Such air may or may not have
been conditioned. (See Air Conditioning.)
Warm Air Heating System : A warm air heating plant consists of a
heating unit (fuel-burning furnace) enclosed in a casing, from which the
heated air is distributed to the various rooms of the building through
ducts. If the motive head producing flow depends on the difference in
weight between the heated air leaving the casing and the cooler air
entering the bottom of the casing, it is termed a gravity system. A booster
fan may, however, be used in conjunction with a gravity-designed
system. If a fan is used to produce circulation and the system is designed
especially for fan circulation, it is termed a fan furnace system or a
central fan furnace system. A fan furnace system may include air washers
and filters.
Wet-Bulb Temperature: The lowest temperature which a water
wetted body will attain when exposed to an air current. This is the
temperature of adiabatic saturation,
Wet Return: That part of a return main of a steam heating system
which is filled with water of condensation. The wet return usually is
below the level of the water line in the boiler, although not necessarily so.
CHAPTER 41 — TERMINOLOGY
ABBREVIATIONS2
Absolute. abs
Acceleration, due to gravity g
Acceleration, linear.— a
Air horsepower air hp
Alternating-current (as adjective) a-c
Ampere amp
Ampere-hour. amp-hr
Area... A
Atmosphere.— atm
Average..... avg
Avoirdupois avdp
Barometer. bar.
Boiler pressure bp
Boiling point bp
Brake horsepower bhp
Brake horsepower-hour bhp-hr
British thermal unit Btu
Calorie -• cal
Centigram eg
Centimeter cm
Centimeter-gram-second (system) . cgs
Change in specific volume during vaporization z>fg
Cubic cu
Cubic foot.... - cu ft
Cubic feet per minute -- cfm
Cubic feet per second cfs
Decibel db
Degree3 .„ - <teg or °
Degree centigrade - C
Degree Fahrenheit F
Degree Kelvin - K
Degree Reaumur - R
Density, Weight per unit volume, Specific weight A or p (rho)
1
P = *V
Diameter D or diam
Direct-current (as adjective) d-c
Distance, linear $
Dry saturated vapor, Dry saturated gas at saturation pressure and temperature,
Vapor in contact with liquid '.....Subscript g
Entropy (The capital should be used for any weight, and the small letter for unit
weight.) -S or ^
Feet per minute fPm
Feet per second ....fps
Foot , - y:«it
Foot-pound *t;lt>
Foot-pound-second (system) - fps
Force, total load f
Freezing point - • *P
Gallon - Sal
Gallons per minute £Pm
Gallons per second - SPS
Gram 3
Gram-calorie ^ - g"cal
*From compilations of abbreviations approved by the American Standards Association, Z, 10 a, c, ft and
i, As a general rule the period is omitted in all abbreviations except where the omission results in the
formation of an English word.
•It is recommended that the abbreviation for the temperature scale, F, C, K, be included in expressions
for numerical temperatures but, wherever feasible, the abbreviation for degree be omitted; as 68 F.
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AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Head .................................................................................................................................... H or h
Heat content, Total heat, Enthalpy. (The capital should be used for any weight
and the small letter for unit weight.) ...................................................................... H or h
Heat content of saturated liquid, Total heat of saturated liquid, Enthalpy of
saturated liquid, sometimes called heat of the liquid ................................................ hf
Heat content of dry saturated vapor, Total heat of dry saturated vapor, Enthalpy
of dry saturated vapor ...................................................................................................... h&
Heat of vaporization at constant pressure .................................................................. L or hfs
Horsepower ................................................................................................................................ hp
Horsepower-hour™ ............................................................................................................... hp-hr
Inch ........................................................................................................................................ v..in.
Inch-pound ............................................................................................................................ in-lb
Indicated horsepower. ............... j ........................................................................................ .....ihp
Indicated horsepower-hour..— ........................................................................................... ihp-hr
Internal energy, Intrinsic energy. (The capital should be used for any weight and
the small letter for unit weight.) .............................................................................. U or u
Kilogram .................................................................................................................................... kg
Kilowatt .................................................................................................................................... kw
Kilowatthour ........................................................................................................................ kwhr
Length of path of heat flow, thickness .................................................................................... L
Load, total ___ ............................................................................................................................. W
Mass ............................................................................................................................................ tn
Mechanical efficiency ................................................................................................................ em
Mechanical equivalent of heat .................................................................................................. /
Melting point ................................................................................................ '. ........................... mp
Meter .......................................................................................................................................... m
Micron ................ r ............................................................................................................... & (niu)
Miles per hour ........................................................................................................................ mph
Minute ...................................................................................................................................... mm
Molecular weight ............................................................................................................ mol. wt
Mol ................................................................................................................................ . ........... mol
Ounce ......................................................................................................................................... .02
Power, Horsepower, Work per unit time ___ . .......................................................................... P
Pressure, Absolute pressure, Gage pressure, Force per unit area ................ . ....................... p
Quantity (total) of fluid, water, gas, heat; Quantity by volume; Total quantity
of heat transferred ............................................................. . ............................... , .............. Q
Quality of steam, Pounds of dry steam per pound of mixture ......................... - ........... . ..... ...»
Revolutions per minute ............................................................ . ........................................... rprn
Saturated liquid at saturation pressure and temperature, Liquid in contact
with vapor .......................................................................................................... Subscript f
Specific gravity .......................................................................................................... , ......... sp gr
Specific neat ........................................................................................................... ,...»,.sp ht or c
Specific heat at constant pressure ............................................................... . .......................... £p
Specific heat at constant volume ................................................................. . .......................... cv '
Specific volume, Volume per unit weight, Volume per unit mass .......... .. ............................ v
Square foot... ................................... . ............................... , ...... , ............... .„,. ....... ,........»„„ ...... sq ft
Square inch .......................................................... „ ............. . ..... „„ ..... „ ...................... ... ...... ....sq in.
Temperature (ordinary) F or C. (Theta is used preferably only when t is used for
Time in the same discussion.)...,. .................. „„.„ ................... . .................... / or 6 (theta)
Temperature (absolute) F abs or K, (Capital theta is used preferably only when
small theta is used for ordinary temperature,) ........... , ......... „„ ____ T or €> (capital tketa)
Thermal conductance4 (heat transferred per unit time per degree),, ......................... .... ..... C
r L j¥ _£_
° " ~R " L " ti ~ it
Thermal conductance per unit area, Unit conductance (heat transferred per
unit time per unit area per degree) ...................................................... . ......... ....... ..... Ca
Cfl « JL m JL _
°a A RA Afa-h) L
<Terms endinff ivity designate properties independent of size or shape, sometimes called spsctyt proper-
te$. Examples are — conductivity and resistivity. Terms ending attcs designate quantities depending
lot only on the material, but also upon size and shape, sometimes called total qv&ntitiw* Example* are —
:onductance and transmittance. Terms ending ion designate rate of heat transfer. Examples are*— con-
luction and transmission.
698
CHAPTER 41 — TERMINOLOGY
Thermal conductivity (heat transferred per unit time per unit area, and per
degree per unit length)
JL.
A
Of \
i — tz)
L
Surface coefficient of heat transfer, Film coefficient of heat transfer, Individual
coefficient of heat transfer (heat transferred per unit time per unit area
per degree) ./
f
7
- /*
(In general / is not equal to k/L, where L is the actual thickness of the fluid film.)
Over-all coefficient of heat transfer, Thermal transmittance per unit area (heat
transferred per unit time per unit area per degree over-all) ...................................... U
Thermal transmission (heat transferred per unit time) ........................................................ q
• -9-
Thermal resistance (degrees per unit of heat transferred per unit time) .......... , .............. R
Thermal resistivity ......................................................................................... . ........................ l/k
Vaporization values at constant pressure, Differences between values for saturated
vapor and saturated liquid at the same pressure .................. , ....................... Subscript fg
Velocity. ....................................................................................................................................... v
Volume (total) ................................................................................................................ .• ........... V
Volume per unit time, Rate at which quantity of material passes through a
machine, Quantity of heat per unit time, Quantity of heat per unit weight ............ g
Watt ......................... » .................................................................................................................. w
Watthour...., ............................................ ... ......... . .................... . ................................ , .............. whr
Weight of a major item, Total weight ...................... > ............................ . .................. . ........... W
Weight rate, Weight per unit of power, Weight per unit of time ...................................... w
Work (total) ..................................................................................................... . ....... . ............... W
CONVERSION EQUATIONS
Fahrenheit degrees « 9/5 centigrade degrees + 32,
Centigrade degrees =» 5/9 (Fahrenheit degrees — 32).
Absolute temperature, expressed in Fahrenheit degrees *» Fahrenheit degrees +
459,6, In heating and ventilating work, 460 is usually used.
Absolute temperature, expressed in centigrade degrees » centigrade degrees -f-
273.1.
Power, Heat, and Work
I ton Deration -
Latent heat of ice » 143.33 Btu per pound
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
1 Btu
1 watthour
1 mean calorie
1 kilowatt (1000 watts)
1 horsepower
1 boiler horsepower
Weight and Volume
1 gal (U. S.)
1 British or Imperial gallon
1 cu ft
1 cu ft water at 60 F
1 cu ft water at 212 F
1 gal water at 60 F
1 gal water at 212 F
1 Jb (avdp)
1 bushel
1 short ton
1 long ton
Pressure
1 lb per square inch
1 oz per square inch
1 atmosphere
1 in. water at 62 F
1 ft water at 62 F
1 in. mercury at 62 F
f 777.5 ft-lb
\ 0.293 watthours
[ 252.02 mean calories
f 2,655.2 ft-lb
I 3.415 Btu
| 3600 joules
{ 860.648 mean calories
0.003968 Btu
3.085 ft-lb
0.0011619 watthours
f 1.3405 horsepower
\ 56.92 Btu per minute
[ 44,252.7 ft-lb per minute
[ 0.746 kilowatt
J 42.44 Btu per minute
1 33,000 ft-lb per minute
[ 550 ft-lb per second
33,471.9 Btu per hour
f 231 cu in.
\ 0.13368 cu ft
277.274 cu in.
7.4805 gal
1728 cu in.
62.37 lb
59.76 lb
8.34 lb
7.99 lb
/ 16 oz
\ 7000 grains
1.244 cu ft
2000 lb
2240 lb
144 lb per square foot
2.0416 in. mercury at 62 F
2.309 ft water at 62 F
27.71 in. water at 62 F
0.1276 in. mercury at 62 F
1.732 in. water at 62 F
14.7 lb per square inch
2116.3 lb per square foot
33.974 ft water at 62 F
30 in. mercury at 62 F
29.921 in. mercury at 32 F
0.03609 lb per square inch
0.5774 02 per square inch
5.196 lb per square foot
I 0.433 lb per square inch
\ 62,355 lb per square foot
10.491 lb per square inch
7.86 oz per square inch
U31 ft water at 62 F
13.57 in. water at 62 F
700
CHAPTER 41 — TERMINOLOGY
Metric Units
1 cm
lin.
1 m
1ft
1 sq cm
1 sq in.
1 sq m
1 sqft
1 cu cm
1 cu in.
1 cu m
leu ft
1 liter
1 kg
lib
1 metric ton
1 gram
1 kilometer per hour
' 1 gram per square centimeter
1 kg per square centimeter (metric atmosphere)
1 gram per cubic centimeter
1 dyne
I joule
1 metric horsepower
1 kilogram-calorie (large calorie)
1 kilogram-calorie per kilogram
1 gram-calorie per square centimeter
1 gram-calorie per square centimeter per centi-
meter
1 gram-calorie per second per square centimeter
for a temperature graduation of 1 deg C per
centimeter
0.3937 in,
2.54 cm
3.281 ft
0.3048 m
0.155 sq in.
6.45 sq cm
10.765 sq ft
0.0929 sq m
0.061 cu in.
16.39 cu cm
35.32 cu ft
0.0283 cu m
1000 cu cm = 0.264 gal
• 2.2046 Ib
' 0.4536 kg
' 2205 Ib (avdp)
> 980.59 dynes = 0.002205 Ib
' 0.6214 mph
/ 0.0290 in. mercury, at 0 deg C
1 \ 0.394 in. water, at 15 C
' 14.22 Ib per square inch
/ 0.03614 Ib per cubic inch
1 \ 62.43 Ib per cubic foot
' 0.00007233 poundals
/ 10,000,000 ergs
! \ 0.73767 ft-lb
/ 75 kg-m per second
: \ 0.986 hp (U. S.)
f 1000 gram-calories (small
' \ calorie)
( 3.97 Btu
• 1.8 Btu per pound
• 3.687 Btu per square foot
' > 1.451 Btu per square foot per inch
[2903 Btu per hour per square foot
M for a temperature graduation of
( 1 deg F per inch of thickness.
SYMBOLS FOR HEATING AND VENTILATING DRAWINGS5
1. The objects of this standard set of symbols are to insure the correct interpretation
of drawings and to conserve drafting room time by establishing simple and unmistakable
symbols for the component parts of the heating and ventilating systems. In preparing
the Hat of symbols an effort has been made to follow existing practice in so far as possible
but the list cannot be expected to match exactly the existing practice of every drafting
room.
2. Simplicity, ease of execution and unmistakable identification were carefully con-
sidered in selecting the symbols. Uncommon fittings and appliances such as vacuum
pumps, separators, etc., have purposely been omitted in order to produce a list which
can be easily remembered. It is assumed that when the scale of the drawing permits,
the valves and fittings will be drawn to scale and a conventional representation is then
unnecessary,
•From A.S.H.V.E, Code of Minimum Requirements for the Heating and Ventilation of Buildings,
edition of 1929,
701
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
3. High pressure steam supply pipe — -
4. Low pressure steam supply pipe '
5. Hot water pipe — flow "*** ----
6. Return pipe — steam or water ------- "-•
7. Air vent line
8. Flanges — :ff—
9. Screwed union — |J|| —
10. Elbow "VH
11. Elbow — looking up Of—*
12. Elbow — looking down @*
13. Tee -fr~
14. Tee— looking up -H©h-
15. Tee — looking down Ol
16. Gate valve ill •
17. Globe valve
18. Angle valve
19. Angle valve — stem perpendicular
20. Lock shield valve ^m\ H^l
21. Check valve
22. Reducing valve
23. Diaphragm valve
702
CHAPTER 41 — TERMINOLOGY
24. Diaphragm valve — stem perpendicular
25. Thermostat
26. Radiator trap — elevation
27. Radiator trap — plan
28. Expansion joint
29. Column radiator — plan
30. Column radiator — elevation
31. Wall radiator— plan
32. Wall radiator — elevation
33. Pipe coil — plan
34. Pipe coil — elevation
35. Indirect radiator — plan
36. Indirect radiator — elevation
37. Supply duct — section
38. Exhaust duct—- section
39. Butterfly damper — plan (or elevation)
40. Butterfly damper — elevation (or plan)
41. Deflecting damper— square pipe
42. Vanes
43. Air supply outlet
44. Exhaust outlet
708
Oh
-9
-I®
f=l
en
n
U iJ
\z\
n
0
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
A.S.H.V.E. CODES
The following codes and standards relating to the design, installation,
testing, rating, and maintenance of materials and equipment used for the
heating and ventilation of buildings, have been adopted by the AMERICAN
SOCIETY OF HEATING AND VENTILATING ENGINEERS:
SUBJECT
TITLE
WHEN ADOPTED
REFERENCE
Air
Cleaning
A.S.H.V.E. Standard Code for
Testing and Rating Air Clean-
June 19o4
A.S.H.V.E. Reprint
Devices
ing Devices Used in General
Ventilation Work
Air purity
Synthetic Air Chart
June, 1917
A.S.H.V.E.
TRANSACTIONS,
Vol. 23, p. 607, and
THE GUIDE, 1931
Standard and Short-Form Heat
A.S.H.V.E.
Boilers
(testing)
Balance Codes for Testing Low
Pressure Steam Heating Solid
Fuel Boilers (Codes 1 and 2)
June, 1929
TRANSACTIONS,
Vol. 35, 1929
A S.H V.E. Performance Test
A S.H.V.E.
Boilers
(testing)
Code for Steam Heating Solid
Fuel Boilers (Code 3)a
June, 1929
TRANSACTIONS,
Vol. 35, 1929
Boilers —
A.S.H V E. Standard Code for
A S H.V.E.
Oil Fuel
(testing)
Testing Steam Heating Boilers
Burning Oil Fuel
June, 1932
TRANSACTIONS,
Vol. 37, 1931
ID '1
A.S.H.V.E. Standard Code for
January, 1929
A.S.H.V.E.
Boilers
(rating)
Rating Steam Heating Solid
Fuel Hand Fired Boilers
Revised
April, 1930
TRANSACTIONS,
Vol. 30, 1930, p. 42
[ Concealed
^ Gravity
A.S.H.V.E. Standard Code for
Testing and Rating Concealed
June, 1934
A.S.H.V.E. Reprint
Type
Radiation
Gravity Type Radiation (Hot
Water Section)
Con vectors
A.S.H.V.E. Standard Code for
Testing and Rating Concealed
Gravity Type Radiation
(Steam Code)
January, 1931
A.S.H.V.E.
TRANSACTIONS,
Vol. 37, 1931, p. 367
Ethics
Code of Ethics for Engineers
January, 1922
A.S.H.V.E.
TRANSACTIONS,
Vol. 28, 1922, p. 6
(See frontispiece
THE GUIDE, 1935)
Fans
Standard Test Code for Disc
and Propeller Fans, Centrifugal
Fans and Blowers
May, 1923.
Revised
June, 1931
A.S.H.V.E.
TRANSACTIONS,
Vol. 29, 1923,
p. 407>>
Garages
Code for Heating and Ven-
tilating Garages
June, 1929
A.S.H.V.E. TRANS-
ACTIONS, Vol. 35,
1929, p. 355
^Originally adopted by the National Boiltr and Radiator Manufactures Association,
o, see Hwtfag, Piping and Air Conditioning, August, 1931, p, 743,
704
CHAPTER 41 — TERMINOLOGY
SUBJECT
TITLE
WHEN ADOPTED
REFERENCE
Heat
transmission
through walls
Standard Test Code for Heat
Transmission through Walls
January, 1927
A.S.H.V.E.
TRANSACTIONS,
Vol. 34, 1928, p. 253-
Minimum
requirements
Code of Minimum Require-
ments for Heating and Ventila-
tion of Buildings, Edition-1929
June, 1925
A.S.H.V.E.
Codes
Pitot tube
Code for Use of Pitot Tube
January, 1914
A.S.H.V.E.
TRANSACTIONS,
Vol. 20, 1914, p. 211
Radiators
Code for Testing Radiators
January, 1927
A.S.H.V.E.
TRANSACTIONS,
Vol. 33, 1927, p. 18-
Unit heaters
Standard Code for Testing and
Rating Steam Unit Heatersc
January, 1930
A.S.H.V.E.
TRANSACTIONS,
Vol. 36, 1930, p. 165-
A S H.V E Standard Code for
A S H V E.
Unit
Ventilators
Testing and Rating Steam
Unit Ventilators
June, 1932
TRANSACTIONS,
Vol. 38, 1932, p. 25
A S H V E Standard Code for
ASH VE Journal-
Vacuum
Heating
Pumps
Testing and Rating Return
Line Low Vacuum Heating
Pumps
June, 1934
Heating, Piping and
Air Conditioning,
March, 1934, p. 136
A.S.H.V.E.
Ventilation
Report of Committee on
Ventilation Standards
August, 1932
TRANSACTIONS,
Vol. 38, 1932, p. 38£
The following Codes and Standards have been endorsed or approved
by the AMERICAN SOCIETY OF HEATING AND VENTILATING ENGINEERS:
SUBJECT
TWLB
SPONSORED BT
RKFBRENCB
Chimneys
Standard Ordinance for Chim-
ney Construction
National Board of
Fire Underwriters
Chapter 14,
THE GUIDE, 1931
Piping
systems
Identification
of Piping Systems*1
A merican Society
of Mechanical
Engineers
Heating^ Piping an&
Air Conditioning,
July, 1929
Warm air
furnaces
Standard Code Regulating the
Installation of Gravity Warm
Air Furnaces in Residences
National Warm
Air Heating As-
sociation
National Warm Air
Heating A ssociation ,
Columbus, Ohio
oAdopted jointly by the Industrial Unit Heater Association, and the A.S.H.V.E.
d Adopted November, 1928, Sponsored by (I) American Society of Mechanical Engineers, (2) Nationa?
Safety Council.
705
INDEX
THE A. S. H. V. E. GUIDE 1935
Technical Data Section
Chapters 1-41 and Pages 1-705
Titles of Chapters
1. Fundamentals of Heating and Air 21. Industrial Exhaust Systems.
Conditioning.
22. Fan Systems of Heating.
2. Ventilation and Air Conditioning
Standards, 23. Mechanical Warm Air Furnace Sys-
tems.
3. Industrial Air Conditioning.
24. Gravity Warm Air Furnace Systems.
4. Natural Ventilation.
25. Boilers.
5. Heat Transmission Coefficients and
Tables. 26, Chimneys and Draft Calculations,
6 Air Leakage 27, Fuels and Combustion.
7. Heating Load. 28. Automatic Fuel Burning Equipment.
8. Cooling Load. 29. Fuel Utilization.
9. Central Air Conditioning Systems, 30* Radiators and Gravity Convectors.
10. Cooling Methods. 3L Steam Heating Systems.
11. Humidification and Dehumidification. 32' PiPinS for Steara Heating Systems.
12. Unit Air Conditioners and Condition- 33- Hot¥ Water Heating Systems and
ing Systems. Piping,
13. Unit Heaters, Ventilators and Coolers. 34. Pipe, Fittings, Welding.
14. Automatic Control. 35. Water Supply Piping.
15. Air Pollution. 36. Insulation of Piping.
16. Air Cleaning Devices. , 37. District Heating.
17. Fans and Motive Power. 38. Radiant Heating.
18. Sound Control 39. Electrical Heating.
19. Air Distribution, 40. Test Methods arid Instruments.
20. Air Duct Design. 41. Terminology.
708
INDEX
TECHNICAL DATA SECTION
(Pages 1 to 705)
Cross Reference to Subjects in
Chapters 1 to 41 Alphabetically
Listed
Air (continued).
Page
A
Page
friction of, in pipes,
327
Abbreviations,
697
impurities in,
84, 259
Absolute humidity,
7
size of,
271
Absorption,
as means of dehumidification,
(see also Regain)
166
ionization of,
leakage,
56
119,126
of solar radiation by glass,
151
mixtures with water vapor,
10
of sound,
303
moist,
45
Acceleration,
685
motion,
51
Acclimatization,
Acoustics, acoustical,
effect of humidity on,
38
299
312
odora in,
optimum conditions,
indoors in summer,
outside, introduced,
33
42
48
treatment,
Adiabatic saturation,
304
14, 166, 184,685
effect on temperature,
fan systems,
54
364, 367
Adsorption,
as means of dehumidification,
685
166
through cracks,
unit air conditioners.
126
212
unit ventilators,
228
Air,
pollution,
259
adlabatic saturation of,
14
abatement of,
263
amount per person,
52
effect on health,
260
atmospheric,
1
primary,
445
changes of, indoors,
cleaning devices,
A,S.H,V.E. code for,
ratings of,
33, 126
271, 685
272
272
properties of,
Quality,
quantity necessary,
for combustion,
2, 4, 49
51
445, 454
requirements of,
271
for ventilation,
52, 500
types of.
273
recirculation of,
55
composition of,
1,33
fan systems,
360, 367
density of,
6
unit, ventilators,
229
distribution of,
317
saturated,
1,5,9,693
A.S.H,V,E. standards,
for comfort,
49
51
secondary,
apace conductances,
445, 473
94
downward,
321
standard,
694
natural ventilation*
83
still,
41
in theaters,
with unit ventilators.
321
220
velocity,
vitiation,
(see Velocity, Air)
83
upward »
321
volume,
10
dry, l,4,8,4fi
ducta, 325 (see Ducts, Air)
washer, 183, 686 (see also Washer , Air)
cooling towers for, 187
exfiltration,
filtration, 119,
flow,
control, principles of,
119,363,479
128,363,479,685
49,51
83
humidifying efficiency,
operation of,
saturation* efficiency,
weight of,
369
252
184
6
as cooling method,
diagrams,
165, 387
325
Air conditioning, 33, 49,
72 ,085 (see also Air)
formulae,
325
air change per occupant,
53
into a hood,
S50
A.S.H.V.E, standards,
49
natural, measurement of,
86
chemical factors,
33, 49
requirements.
84
comfort chart,
44,46
tables,
325
functions of,
201
through openings,
78,83
fundamentals of,
1
709
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Air conditioning (continued),
industrial,
apparatus for,
automatic control,
exhaust systems,
of libraries,
plants,
process conditioning,
of railroad cars,
temperature differential in,
unit air conditioners,
objective of,
physical factors,
recirculation of air,
standards,
Algae formations,
Alumina system of adsorption,
Aluminum foil,
Ammonia,
Anemometer,
Anthracite,
Apartment houses,
hot water supply to,
stokers suitable for,
Aquastat,
Area of:
chimneys,
fittings,
grates,
human body surface,
leader pipes,
pipe,
registers,
stacks,
wall surfaces,
A.S.H.V.E. Codes and Standards,
48, 88, 2
A.S.M.E, boiler construction code.
Asbestos,
Ash,
cared for by stokers,
ny,
Atmosphere, standard,
Atmospheric steam heating system,
Atmospheric water cooling apparatus,
design of,
efficiency of,
Atoraization,
for humidifying,
of oil,
Audiometer,
Automatic control,
Automatic fuel burning equ
Awninga,
B
Bab cock's formula for steam flow,
Baffles,
Bananas, ripening of,
Barn ventilation,
Barometer,
aneroid,
mercurial,
Baudelot,
chamber,
heat absorber,
Bends, expansion,
BET, British equivalent temperature.
Blast,
Blower, blowers,
standard teat code for.
Blow-through heating units,
Body, human, surface area,
Boiler, boilers,
A,S,H.V,E, test codes,
A.S.M.E. construction code,
baffiles,
capacity,
care during summer,
cleaning,
connections,
conversion,
design of,
domestic oil burners,
«0, Page
Boiler, boilers (continued),
Page
65
draft loss through,
435
72
efficiency of, 409,
411,480
250
for electric steam heating,
670
845
fittings,
416
70
gas- fired, 407,
415, 471
195, 262
heat transfer rates,
' 400
65, 167
heating surface, 409,
474, 686
201
horsepower,
686
lin, 159
installation,
415,417
200
insulation,
420
1,48,58
low pressure, construction code,
416
33,49
oil burners,
406, 470
55,246,366,382,472
operation,
41S
33,49
output,
410
191
performance curves,
413
on, 169
ratings of,
410,475
113
runouts, sizes,
545
188, 597
scale in,
419
678, 686
selection of,
414
443, 447 (see also Coal]
settings,
408
troubles with,
418
617
types of,
405, 670
459
warming-up allowance,
412,414
469
water line,
416
Booster,
430, 440
coils,
361
587
fans.
156, 402
371, 383, 396, 414, 690
Bourdon tube,
675
52
Boyle's law,
5
391
A91
Brake horsepower.
OjiJL
fan,
187
393
393
heat equivalent of,
Branch connections,
138
505
92
Breeching, draft loss through,
435
ndards,
:8, 88, 272, 284, 498, 704
n code, 417
Brine,
British equivalent temperature,
British thermal unit,
177, 236
659
086
626
Building, buildings,
457
air velocities in.
331
260
classification for district heating,
651
70
construction, heat transmission of,
93,97
system, 511,539,547
ipparatus, 186
188
district heating,
fuel requirements of
heat capacity of,
644
470, 482
481
189, 190, 194
hot water supply to,
intermittently cooled,
611,016
149
73
intermittently heated, 139, 385,
481, 672
463
materials, heat transmission of,
94
301
noise in,
301
239 (see also Control1)
ipment, 457
380
saving of steam in,
tall, infiltration in,
water supply to,
645
126
599
Burner, burners,
automatic equipment,
457
coal.
457
sam flow, 527
conversion,
473, 475
377, 686
gas,
471
71
oil,
469
87
By- pass method,
156, 686
675
675
C
185
Cabinets, ($e$ Enclosures)
177
Calorie,
686
542, 583
Calorific values,
aperature, 659
coal,
444
686
gas,
453
28 1 (see also Pans)
284
oil,
Carbon dioxide,
451
188
361
concentration in air,
51
52
as corrosion agent,
595
ilftfi RRft
as an index on
wVt), ODD
410, 704
combustion,
draft loss,
445
435
Je, 410
377, 686
405
odors,
measurement of.
33
(181
419
Carbon monoxide,
418
in air,
260
416, 543
in garages,
SS
415, 470
408
poisoning,
produced by oil burners.
261
404
406,470
Cattle, heat and moisture produced by,
87
710
ALPHABETICAL INDEX TO TECHNICAL DATA SECTION
Page
Ceilings, heat transmission, 107
Central air conditioning systems, 155, 197
automatic control of, 244, 252
design of, 157
location of apparatus, 158
ratings of, 162
spray type, 156
Central fan heating systems, 359, 686
computations for, 366
design of, 363
electrical, 669
heating requirements of, 362
Charles' law, 7
Chart,
of air densities, J
comfort, 44, 51
effective temperature, . 40
psychrometric, _ t 19« insert
Ringelmann, of smoke densities, 682
thermometric, 40
Chimney, chimneys, 423
areas of, 430,440
characteristics, 425
construction of, 438
Combustion,
air required for,
of different coals,
of gas,
of oil,
smokeless,
with various stokers,
Comfort,
chart,
effective temperature,
heating for,
level,
line,
for men working,
optimum air conditions for,
school children,
effect,
efficiency of,
performance,
sizes,
Venturi,
Cinder, cinders,
catching devices,
disposal of,
78,81,119,126,517,686
426, 480
429
430, 440
425
260
265
267
Circular equivalents of rectangular ducts, 333
Circulator, 472
Classrooms, (see Schools)
Cleaners, air (see A »>, Cleaning Dt, vices)
Clearance, window sash, 122
Coal, (see also Anthracite; Coke; Lignite)
analysis of, 443
bituminous, 448
calorific value, 444
classification of, 443
dust, disposal of, 267
dustless, 450
pulverized, 450
semi-bituminous, 449
size of, ' 445
Coal burning systems,
automatic control of, 247
automatic firing equipment, 457
boilers, 405
combustion rate, 376
draft required for, 434
estimates of heating costs, 488
fuel requirements, calculation, 479, 485
furnace requirements, 370, 383
hand-fired, 450
stokers, 457
Codes, ,
A.S.H.V.E. codes and standards, 704
for grinding, polishing, and buffing wheels, 348
for proportioning warm air heating plants, 471
for use of refrigerants, 157
Coefficients of heat transmission,
(see Heat Transmission, Coefficients}
Coils,
booster, owl
cooling, 211, 379
evaporator, 211
heating, 213, 301
hot water, 204
pipe, 549
radiator, 491
steam, 20$
Coke, 444
combustion of, 450
Cold, effects on human body, 36
Collectors, dust, 354
Combined system,
air conditioning equipment, 229, 318
automatic controLof, 246
central f an, %$®
Page
443
445, 454
447
453
467, 470
409
457
38
44, 46, 51
' 39
657
495
43, 46, 48, 687
46
42,46
46
zone, 43 (see also Zone, Comfort}
Compliance, of sound insulating materials, 310
Compressed air, 73
Compressors, 211
reversed refrigeration, 671
types of, 175
Condensation,
on building surfaces, 139
meters, 649
prevention of, 141, 632
rate in radiators, 495
return pumps, 518
in steam heating systems, 503, 527
in winter, 46
Condenser, 202
design data, 178, 188, 211
turbine, 186, 190
water temperatures, 189
Conditioning and drying,
67 (see also Air Conditioning)
Conductance, 92, 113, 687
of air spaces, 94
of building materials, 95
of insulation, 95, 624
surface, 694
Conduction, 491, 687
Conductivity, 92, 113, 687
Conduit, 641
Connections,
for boilers, 416, 543, 545
branch, 505
for central fan systems, 549
for chimneys, 440
for convectors, 549
for district heating systems, 644
for drains, 416
Hartford return, 543
for hot water systems, 576
for indirect heating units, 551
for pipe coils, 549
for radiators, 547, 572
Construction code for low pressure boilers, 416
Control, controls,
accessory automatic apparatus, 242
of air conditioning equipment, 239, 250
combined system, 246
split system, 244
automatic, 213, 239, 243, 250
connecting apparatus, 242
of cooling units, 260
of electrical heating, ' 672
of fan motors, 295
manual, 81, 213
of mechanical warm air systems, 3S3
of natural ventilation, 81
of oil burning equipment, 465
of sound, 299
of ateara heating systems, njn jrtw 517
of temperature, 243, 465, 672
of Unit conditioners* 213
«. ,472, 657, 668, 687
Convectora, 491,496,687
connections for, 649
design of, 497
gravity, 491
hemt emission by, 491, 498
711
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Convectors (continued), Page
heating capacity, 498
performance characteristics, 497
Conversion equations, 699
Coolers,
surface, 162
types of, 177
unit, 234, 695
Cooling, 14, 19
with central fan heating systems, 379
effective temperatures for, 50
equipment, design of, 188
evaporative, 72, 155, 165, 184
of fluids, 189
of human body, • 35
load, 145, 214
with mechanical warm air systems, 387
methods, 155,165,202
ponds, 190
relative humidities for, 50
towers. 174, 179, 187, 190
water, 188
Copper pipe, 580
Corrosion,
of boilers, 419
of industrial exhaust systems, 356
inhibitors, 597
of pipe, 595
tester, 596
Costs,
comparative, of fuels, 488
of district heating service, 652
of electrical heating, 673
of unit conditioners, 215
Crack, window, 122
Cyclone dust collector, 354
Dal ton, law of partial pressures, 1
Damper, dampers,
apparatus which operates, 242, 244, 246
control, 80
in duct systems, 881
types of, 381
with unit ventilators, 228
Decibel, 299, 687
Definitions, <685
Degree-day, 687
industrial, 485
method of estimating fuel consumption, 483
records for cities, 484
Dehumidification, 14, 183
effective temperatures for, 50
methods of, 155, 166, 202
relative humidities for, 50
Dehumldlfier, dehumidifiers, 166, 688
alumina, 169
in central air conditioning systems, 156
in industrial air conditioning, 72
silica gel, 168
types of, 74
Density, 2,688
of air, 6
of saturated vapor, 10
aped fie, 3
of water, 20
Design temperature,
dry-bulb, 147
wet-bulb, H7, 189
Dew point, 688
relation to relative humidity, 9
temperature* 2, 251
Diameter, circular equivalents of rectangular
ducts, 834
Dichlorodifluoromethane, 175, 188
Diesel engine, 190
Dirt pockets, 655
Disc fans, test code for, 284
Distribution of air, 317 (see also A ir, Distribution}
District heating, 639
DIverter, back draft, 439
Page
Domestic supply,
hot water, 468, 617, 671
water, 599
Doors,
air leakage through, 122
coefficients of transmission of, 113
natural ventilation through, 80
Down-feed piping systems, 506, 508, 510, 513
Downward system of air distribution, 321
Draft,
available,
back, diverter,
calculations,
capacity,
intensity required,
in chimneys,
through fuel bed,
mechanical,
natural,
theoretical,
towers,
Drain connections,
Draw-through heating units, *
Drawings, symbols for,
Dripping of steam pipes,
Dry-bulb temperature, (see Temperature, Dry-bulb}
Dry return, 688
Drying, 67 (sec also Regain)
423
425, 432
439
423
425
676
688
434, 447
432
436
433
425
423
425
192
416
361
701
555
of lumber,
Duct, ducts,
air,
design of,
equal friction method,
velocity method,
for air distribution,
air velocities in,
circular equivalents,
construction details,
design of duct systems,
humidity measurement In,
noise transmission through,
pressure loss in,
for recirculated air,
sheet metal for,
sizes of,
temperature loss in,
temperature measurement in,
velocity measurement in,
Dust,
catching devices,
collectors,
concentration in air,
counter,
disposal of,
industrial exhaust systems,
measurement of,
71
325
325, 330
331,333
331
317
342
330, 340, 380, 393
681
311
320
393
352
320,333,347
365, 391
677
678
40,250,688
265
354
271,081
681
267
345
681
Dynamic equilibrium, Carrier's equation for,
E
EDR, equivalent direct radiation, 694
Effective temperature, (M« Tempsrature, Rffetilm)
Elbow, elbows,
design of, 380, 590
equivalents, 503
loss of pressure in, 326
resistance in, 354
sheet metal used in, 352
welding of, 591
Electric, electrical,
central fan heating systems, 009
current, as corrosion agent, 595
heat equivalents, 673, 700
heaters, capacity of, 673
heating, 007
auxiliary, 072
of hot water, 071
heating elements, 205» 697, 000
with unit heaters, 220
lamp bulbs, heat from, 139
712
ALPHABETICAL INDEX TO TECHNICAL DATA SECTION
Page
Page
Eliminator plates and baffles,
183, 187
Fatigue, human, 37
Emissivity,
Enclosures,
660
Filter, filters, 212, 267
automatic, 275
concealed heaters,
497
cloth, 354
convectors,
497
design of, 212, 274
effect of,
495
dry air, 27&
unit air conditioners,
210
installation of, 277
Engines,
resistance of, 379
Diesel,
190
for sound, * 311
internal combustion,
Enthalpy,
Entropy,
189
18, 689
23, 689
unit type, 274
viscous type, 274
Fire walls, 352
Equations, conversion,
Equilibrium,
699
Fittings, 579 (see also Connections; Pipe)
areas of, 587
dynamic,
2
flanged, 589
hygroscopic,
70
lift, 514
Equipment room, design of,
307
screwed, 587
Equivalent, equivalents,
welding, 592, 594
circular,
333
Flame, with oil burners, 464, 469
direct radiation,
138, 559, 694
Flanges, welding neck, 592, 594
elbow,
evaporation,
heat,
563
411, 689
699
Floors, heat transmission through, 107
Flowers, temperatures for greenhouses, 72
of 'air infiltration,
128
Fluid, fluids,
of brake horsepower,
electrical,
138
673, 700
cooling of, 189
formula for flow of, 325
mechanical,
692
meters, 648
length of run,
351
Foodstuffs,
square feet,
492
regain of moisture of, 66
Ethylene gas, in ripening bananas
3, 71
temperatures and humidities for processing, 68
Eupatheoscope,
663, 672, 683
Force, 689
Evaporation,
26, 28, 72, 193
Forge shops, heat given off in, 83
equivalent,
411,689
Formulae, conversion, 699
from human body,
35. 59
Foundries, heat given off in, 83
rate of,
from water pans,
Evaporative cooling,
Evaporators,
26
496
72,155,165,184
211
Freezing,
of cooling water, 193
insulation against, • 631
Exfiltration,
119,303,479
Friction,
Exhaust systems,
industrial,
Expansion,
of joints,
of pipe,
in steam piping,
345
346, 351
542, 641
542,581,641
541
in chimneys, 428
coefficients, 329
heads in pipes, 562
in heating units, 362
losses in ducts, 327, 329, 333
in water pipes, 606
tanks,
574
Fuel, fuels, 443 (see also Anthracite; Coal; Coke;
Exposure factors,
135
Gas; Lignite; Oil}
bed, draft loss through, 433
F
burning equipment, automatic, 457
Fan, fans,
281
comparative heating costs, 488
requirements, 479
as accessory apparatus,
A.S.H.V.E. test code for,
attic,
booster, equipment,
198, 609
284
233, 380
150, 402
degree-day method, 483
method of approximation, 485
saving during non-heating periods, 481
utilization of, 479
brake horsepower,
control of,
for cooling,
designation of,
drives, arrangement of,
187
291
380
291
292
Fumes, 259, 689
industrial exhaust systems, 345
toxicity of, 263
Fundamentals of heating andjair^conditioning, 1
dynamic efficiency of,
efficiency of,
283
283
Furnace, furnaces, 689
design of, 376, 383, 396, 408, 451
in electrical heaters,
689, 672
door slot openings, 446
furnaces,
375, 387
efficiency of, 480
for gas- fired furnaces,
for industrial exhaust systems,
472
355
hand-fired, 451
performance curves of, 397
mechanical draft.
425
ratings of, 387
mechanical efficiency of,
283
types of, 375, 387, 471
motive power of»
293, 296
volume, 689
control of,
295
for warm air systems, 375, 396
mountings,
295
Furnacestat, 383
operating characteristics,
284
operating velocities,
289, 290
G
performance of,
quietness of,
ratings of,
281,289
225
288
Gage* gages,
draft, 676
selection of,
287,290,293
pressure, 675
static efficiency of,
283
Steam, 416
systems of heating,
tip speeds,
859
289
vacuum, 675
Galvanometer, 676
total efficiency of,
283
Garage, garages,
types of,
281,286,289,402
air flow necessary in, 84
in unit conditioners,
212
A,S.H,V,E, ventilation code, S8
In warm air systems,
377, 886, 402
heaters for, 473
713
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Page
Heat (continued),
Page
Gas, gases,
exchanger,
186, 188
calorific value,
139, 453
shell and tube,
177
in chimneys,
428
flow meter,
92, 683
flue, analysis,
682
gain,
fuel,
from fixtures and machinery,
153
manufactured,
453
from outside air,
153
natural,
453, 480
to be removed,
161
454
sources of,
214
scrubbers,
267
infiltration equivalent of,
128
toxicity of,
263
latent,
690
Gas-fired appliances,
accessory conditioning equipment,
automatic control of,
205, 248
199
247, 471
loss,
of water vapor,
of the liquid,
57
10
23, 691
boilers 407
415, 471
loss,
selection factors,
carbon monoxide produced by,
chimneys for,
classification,
control of,
conversion burners,
furnace requirements for,
heating costs, estimates of,
installation,
rate of gas consumption,
ratings of,
types of space heaters,
used with unit heaters,
warm air furnaces,
Gaskets,
474
475
438
470
472, 474
473, 475
376, 3S3
488
475
474, 486
475
472
226
471
590
from bare pipe,
computation of, 91, 140,
determination of, 131, 138,
effect of insulation on,
from human body, 57,
by infiltration,
by intermittently heated buildings,
latent,
from piping of gas-fired furnaces,
by radiation,
sensible,
to unheated rooms,
maximum probable demand,
mechanical equivalent of,
of the liquid,
produced by cattle,
021
600, 072
479, 057
033
657, 059
128, 479
385
57
474
41, 657
67, 659
116
131
692
23, 691
87
Glass,
heat transmitted through,
113, 152
produced by human body,
pump,
34
671
solar radiation through,
149
radiation,
693
window, area,
92
regulation in man,
34, 38
Glossary of terms,
685
sensible,
165, 690
Grates,
690
of air,
10
areas of, 371,383,396,
414, 690
loss,
57, 659
of furnaces, 371,383,
396,414
solar,
146
of stokers,
457
sources of,
657, 670
Gravity
other than heating plant, 138,
170, 482
491
total,
15, 251
gravity-indirect heating systems,
499
of saturated steam,
transmission,
23
91, 657
specific, —
steam heating systems, 503
one-pipe air-vent, 503, 500, 535, 547
two-pipe air-vent, 507, 536, 547
warm air heating systems, design of, 389
Greenhouses, temperatures for, 72
Grille, grilles, 690 (see also Rt&isters)
anemometer readings through, 679
through air spaces,
through building materials,
calculations,
coefficients,
of ceilings,
combined,
of doors,
of floors i
94
94
91
91,114
107
115
113
107
for concealed heaters,
498
95
of roof ventilators,
80
of roofs,
110
for warm air systems,
317, 393
of skylights,
113
of walls,
100
H
of windows,
113, 152
convection equation,
658
Hartford return connection,
Health, effect of air pollution on,
505, 545
260
definition of terms used,
effects of solar radiation on,
92
148
690
formulae »
02
absorbed by building: structure,
air infiltration equivalent of,
capacity, 60,
of buildings,
of leader pipes,
139
128
149, 690
481
391
through glass,
measurement of,
in surface coolers,
by surfaces not exposed to the sun,
symbols used in formulae,
to IKl/ke
113, 152
683
103
146
92
c>i
conduction,
687
13.O1CS,
time lag,
iff A
149
of air and water vapor,
of dry air,
of saturated water vapor,
convection,
conversion equations,
demand, factors governing,
effects on human body,
electrical equivalents of,
emission,
10
15
18
687
699
131
35
673, 700
Heaters,
for domestic hot water, 616
electric, 86S
capacity of, 673
radiant, 472, 672
space, 472
unit, . 219, 695
wall, 472
Heatinft, ' (set aha Haai}
of convectors.
491,498
costs, relative.
488
by radiation,
660
district,
264,630
of radiators,
491,498
effect of radiators,
408
equivalent, equivalents,
of air infiltration.
699
128
electrical,
elements, electric,
$67
OSS
of brake horsepower,
138
fundamentals of,
1
electrical,
673, 700
load.
m
mechanical,
692
medium,
600
714
ALPHABETICAL INDEX TO TECHNICAL DATA SECTION
Heating (continued},
radiant,
by reversed refrigeration,
surface,
square foot of,
systems,
district,
electrical,
fan,
gravity warm air furnace,
hot water,
mechanical warm air furnace,
radiant,
steam,
units,
blow-through,
central fan,
draw-through,
Henry and Dalton, law of,
Hoods,
axial velocity formula,
canopy,
design of,
for exhaust systems,
of furnaces,
Horsepower,
boiler,
brake,
fan,
heat equivalent of,
Hot box,
Hot plate,
Hot water heating systems,
forced circulation,
gravity circulation,
installation of,
mechanical circulation,
Hot water piping,
Hotels,
stokers suitable for,
temperatures of in winter,
water supply,
Humidincation,
atomizatlon for,
effective temperatures for,
methods of,
relative humidities for,
for residences,
systems of,
with water pans,
in winter,
Humidifier, humidifiers ,
with fan systems,
. types of f
with uriit air conditioners,
Humidistat,
Humidity,
absolute,
effect of on acoustics,
for industrial processing,
measurement of,
relative, 8, 691 (see aU
A.S.H,V*B. standards,
in comfort zone»
effect on moisture regain,
relation to dew point,
specific,
Hygrodeik,
Hygroscopic materials,
with duatleas coal,
moisture content,
proteasing of,
regain,
Hygrostat,
Ice. in air conditioning,
Inch of water,
Industrial,
air conditioning,
apparatus for,
automatic control of,
air pollution,
Page
Industrial (continued),
Page
657, 668
cooling systems,
167
206
degree-day,
485
409
drying,
67, 290
694
electrical heating systems,
671
exhaust systems,
345
639
heat sources,
138
667
plants,
65
359
proceSvSing of hygroscopic materials,
67
389
temperatures and humidities for,
68
559
unit heaters,
226
375
Infants, premature,
43,45
657
Infiltration,
6S5
503
average,
126
fuel utilization,
479
361
heat equivalent,
128
361, 669
through shingles,
121
361
through walls,
120
595
through windows,
123
Institutions, water supply to,
601
349
Instruments,
675
350
349
Insulation,
691
345
asbestos type,
377
corrugated,
626, 627
laminated,
628, 629
691
of boilers,
420
411,430,686
bright metal foil,
113
characteristics of,
95, 625
187
effect on heat loss,
633
138
92, 683
683
with electrical heating,
heat transmission through,
for low temperatures,
667
95, 625
624
559
magnesia type,
625
561
569, 573
575
573
of piping, 621
to prevent condensation, 139, 141, 632
to prevent freezing, 631
reflective type, 113
559
rock wool type,
630
of sound,
304
460
tables.
95, 625
132
thickness needed,
634
599
types of,
96
14, 183
underground,
635
73
of vibration,
308
50
Internal combustion engines,
189
202
lonization of air,
, 56
50
Isobaric,
691
252, 496
Isothermal,
7,691
194
496
157, 496
J
309
Joints, expansion,
542, 641
72
212
K
241,383,691
7t 658, 691
Kata thermometer,
51, 679
7,691
Kiln drying of lumber,
72
312
68
680
L
Relative Humidity}
Latent heat,
losa,
690
67
45
of water vapor,
10
9
Lead poisoning,
262
8,691
681
Leader pipes,
heat carrying capacity of,
size of,
389
391
391,401
67
450
Leakage of air, 119 (see also
Infiltration)
65,66
Length of run, equivalent,
531
67
Libraries, air conditioning of,
69
65,66
Lignite,
444
241, 691
Liquid, heat of the,
23, 691
Load,
cooling,
60, 145
178,204,379,387
AQl
design,
heating,
410, 689
131
UUJ,
hot water supply,
413
05
72
radiation,
412, 68fl
412
250
Louver fences,
ISO
301
Lumber, drying of,
71
716
AMERICAN SOCIETY of HEATING and
VENTILATING ENGINEERS GUIDE, 1935
M
Page
Oil, oils (continued), Page
Machinery,
air supply for, 463, 467
as heat source,
138, 153
automatic, 469
sound insulation of,
307, 309
boilers, 407, 409, 466
Magnesia insulation,
625
carbon monoxide produced by, 464
Manometer,
Masonry materials, heat transmission
678, 69 1
through, 95
for commercial use, 469
control of, 247, 465
for domestic hot water supply, 468
Mass,
692
for domestic use, classification, 462
Mb,
559,692
estimates of heating costs, 488
Mbh,
559, 692
flame with, . 464
Mean radiant temperature,
657, 660
furnace requirements, 376, 383
Mechanical,
installation, 467
draft towers,
equivalent of heat,
warm air furnace systems,
192
692
375
maintenance, 468
oil consumption. 469, 479, 485
operation, 464, 469
Metabolism,
35,56
Orsat test, 467
specifications, 451
Meters,
calorific value of, 451
choice of,
648
classifications, 451
condensation,
649
as corrosion inhibitor, 597
fluid,
648
cost of, 453
Nicholls heat flow,
683
heated electrically, 671
steam flow,
650
ignition of, 452
types of,
648
preheating, 469
Methyl chloride,
188
specifications, 451
Metric units,
701
One-pipe steam heating systems,
Micron,
692
gravity air-vent, 503, 506, 535, 547
7fl
down-feed, 506
Mildew,
{ U
up-feed, 504
Mixture, air and water vapor,
10
vapor, ' 508
Moisture,
632
Openings,
content,
air inlet, 80
of air, . . 5
2, 65, 72, 165
monitor, 80
as index of air distribution,
51
for natural ventilation,
of hygroscopic materials,
66
location of, 83
loss by human body,
57,59
resistance offered to flow, 84
from outside air,
153
size of, 77
produced by cattle,
87
types of, 78
regain,
65
Ori6ce, orifices,
Mol,
692
friction heads, 568
Monitor openings,
80
steam heating systems, 510, 529, 539, 547
Motive power,
281
Orsat test apparatus, 467, 682
Motors,
293
Outlets, (see also Registers; Grilles)
classification of,
294
design and location of, 169
for fan operation,
293
Oxygen, 595
as heat source,
138, 153
of unit air conditioners,
210
P
MRT, mean radiant temperature,
657, 660
Paint,
effect on radiators, 493
spray booths, 351
temperatures and humidities for processing, 69
Natural draft towers,
192
Partial pressures, Dalton's law of, I
Natural ventilation,
77
Perspiration, 35, 04, 58, 60
Nicholla heat flow meter,
683
Petterson-Palmquist apparatus, 681
Noise, (see
also Sound)
Phon, 300
in buildings,
control of,
through ducts,
with warm air systems,
1*kV*»l
301
303
311
378
Pipe, piping, 579
bare, heat loss from, 621
bends, 542
capacities, (set Pipe, Siws)
jeVcl,
acceptable,
of compressors,
of fans,
of unit heaters,
of various apparatus,
measurement of,
Nozzle,
air spray^
oil atomiser,
water spray,
303
175
288
225
302
300
183
139, 322
470
73
conduit, 041
connections, 643, 644 (see also Connections)
corrosion of, 595
dimensions of, 580, 821 (w* also Pipt> Si&$$)
down-feed systems, 506, SOS, 510, 513
expansion of, 541,581.041
fittings, 580 (see also Connections; Fittings)
for water supply, 604
welding fittings, 590, 621
flexibility of, ' 581
,
friction,
O
of air in, 327
Odors,
51
heads in, 563
of human origin,
concentration,
removed byloutsJde air,
on, oils,
33
54
54
gaskets, 501
hangers, 585
heat loss from, 474, 621
for hot water heating systems, 559, 575
insulation of, 621
atomi»ation of,
463
Joints, 542. 641
burner, burners,
leader, 391
accessory conditioning apparatus,
109
radiators, 491
air for combustion,
407
scale in, 595
ALPHABETICAL INDEX TO TECHNICAL DATA SECTION
Pipe, piping (continued},
sizes,
for boiler runouts,
for central fan systems,
for conyector connections,
dimensions,
for district heating,
for domestic hot water,
effects of variation of,
elbow equivalents,
equivalent length of run,
friction head,
of orifices in unions,
for Hartford return connection,
for hot water heating systems,
forced circulation systems,
gravity circulation systems,
for indirect heating units,
for pipe coil connections,
for radiator connections,
return, capacity of,
Page Pressure, pressures (continued},
Page
steam,
underground,
tables,
tees,
for underground steam,
for water supply,
weights,
steam, capacity of,
for steam heating systems,
supports,
sweating,
systems, down-feed,
systems, up-feed ,
tax,
tees, dimensions of,
threads,
tunnels,
types of,
underground,
insulation of,
steam,
for unit conditioners,
for unit heaters,
up-feed systems,
valves,
water supply,
weights of,
welding,
Pitot tube,
steam,
545 in district heating, 640
549 drop, 505, 528, 533
549 initial, 528
580, 582 in orifice systems, 516
640 saturated, , 23
611 in sub-atmospheric systems, 515
567 total, 695
563 vapor, 27, 696
531 velocity, 696
564 water, 26, 602
568 Processing, 65
543 cooling systems, 167
560 industrial, temperatures and humidities for, 68
562 of textiles, 67
569 unit air conditioners, 200
551 unit heaters, 227
549 Propeller fans, test code for, 284
547 Psychro meter, 693
534 sling, 680
Psychrometric,
chart, insert
explanation, 19
tests, 39
Pump, pumps,
circulating, 573
condensation re-turn, 518
heat, 671
vacuum, 515
ratings of, 519
Pyrheliometer, 146
Pyrometer, . 677, 693
mercurial, 677
optical, 677
radiation, 677
thermo-electric, 677
528, 532, 533
639
533, 582
587
639
602
580
529
503, 527
585
632
506, 508, 510, 513
504,507,509,512
413
587
585, 589
643
579
635
639
213
225
504,507,509,612
592
599
680
590
• 678
Plastering materials, heat transmission through, 97
Plenum.,
chamber, ' 692
systems, automatic control of, 246
Plumbing fixtures, 599
Pollution of air, 259
Ponda, cooling, 190
Potassium permanganate, 191
Potentiometer, 676, 692
Power, 692
conversion equations. 699
electric, 073
Preclpltators, dust, 266
Pressure, pressures,
absolute, 085
in heating unit, 362
measurement of, 678
apparatus sensitive to, 241
atmospheric, 675, 686
for atomizauon, 18*
barometric, 428, 676
basic, 8
conversion equations, 700
drop, formula for, 640
dynamlc' AM Aon
gage, 675, 690
loss through ducts, 325
measurement of, 675
partial* Daiton'a law of, 1
refrigerating plant, 188
of saturated vapor, 10
static, 371, 694
Quality,
of air, 51, 55
A.S.H.V.E. ventilation standards, 49
impaired by recirculation, 55
Quantity,
of air,
A.S.H.V.E. ventilation standards, 49
blown by wind, 77
measurement of, 678
necessary for ventilation, 52, 54, 83, 159
of cooling water, 188
Radiant heat, 472
thermometric chart does not apply, 41
Radiant heating, 657
Radiation, 693
by black body, 660
direct, control of, 243
equivalent direct, 138, 559, 694
heat loss by, 41,657
by human body, 38, 41, 59T 657
as index of fuel consumption, 485
load, 412
with oil burners, 464
by radiators, 491
solar, . 146
curative value of, 56
effect on heat transmission, 148
occlusion of, 261
Radiator, radiators, 491,693
A.S.H.V.E. code for, 498
column, 687
condensation rate in, 495
connections, 547, 572
enclosed, " 495
Cared, 473
i emission of , 491,498
heating capacity of, 498
heating effect of, 493
for hot water systems, 569
717
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Radiator, radiators (continued),
Page
Resistance,
Page
output of,
paint, effect of,
492
493
of bright metallic surfaces,
of building materials,
113
95, 632
ratings of,
492
in ducts,
354
shields,
496
of exhaust systems,
355
types of,
491
of filters,
379
warm air,
473
of insulators,
95, 632
Rain, as dust catcher,
268
of sound-insulating materials,
308, 310
thermal,
694
Ratings,
Resistor,
667, 671
of air cleaning devices,
272
Restaurants,
of boilers,
410,475
tobacco smoke in,
52,212
for central fan conditioning,
162
water supply to,
618
of concealed heaters,
497
Return,
of fans,
288
dry,
688
of furnaces,
387
pipe, capacity,
534
of gas- fired appliances,
475
wet,
696
of noises,
302
Ringelmann chart,
682
of pressure reducing valves,
539
Rock wool insulation,
630
of radiators,
492
Roof, roofs,
for surface coolers,
162
coefficients of transmission of,
110
for unit air conditioners,
214
conductivities of,
97
of unit coolers,
236
solar radiation on,
148, 150
of unit heaters,
223
ventilator,
80
of unit ventilators,
231
of vacuum pumps,
519
S
Receivers, alternating,
524
Refrigerants,
693
Salts in cooling water,
187
codes for use of,
types of,
Refrigerating capacity,
Refrigerating plant,
157
176,211,379
170
186, 188
Scale,
in boilers,
centigrade,
on equipment,
Fahrenheit,
419
676
187
676
compressor,
190
in pipe,
595
operating methods,
171
Reaumur,
676
size of,
171
School, schools,
steam jet system,
173, 190
air distribution in,
317
Refrigeration,
air flow necessary in,
84
cycle,
167
optimum air conditions,
46
dehumidification by,
diagram of,
106
167
stokers suitable for,
temperature of, in winter,
460
132
direct expansion system,
202,215
ventilation in,
46, 310
indirect expansion system,
203
Scrubbers,
267, 273
mechanical,
202
air,
183
reversed,
steam jet,
206, 671
204, 675
Sensible heat,
105, 600
ton of,
170, 605
of air.
10
ton-day of,
unit coolers,
vacuum,
695
234
204
loss,
Settling chamber,
Sheet metal, for ducts,
57, 651)
260
352
Shingles, air leakage through,
121
of hygroscopic materials,
standards of commercial,
Registers, 603
66
70
(see also Grilles)
Silica gel,
regain of moisture of,
system of adsorption,
Silicosis,
66
168
262
with gas- fired furnaces, 472
with mechanical warm air furnace systems, 381
sizes, ' ^Q<9 A'"11
Sizes of pipe,
" Skylights,
(m Pipe, Sims)
80, 113
and stacks.
81
Sling psychrometer,
680
of unit air conditioners,
210
Smoke,
259, 098
Reheatcrs
161
abatement of,
263
measurement of,
082
Relative humidity,
50, 691
recorders,
082
apparatus sensitive to,
241
tobacco,
52, 212
A.S.H.V.B. standards,
49
Solar heat,
146
for banana ripening*
in comfort zone,
control of,
71
45,48
251
Sound,
absorption coefficients,
299
803
effect on sound,
in industrial plants,
of libraries,
for lumber drying,
mildew
812
65
70
72
70
control,
effect on duct design,
effect of humidity on,
effect of temperature on,
insulation of,
299
341
B12
312
804
for processing,
in public buildings,
in residences,
68,70
48
496
intensity,
measurement of,
in steam heating systems,
399
aoo
580
for textile testing
70
Specific density,
3
from water pans,
496
Specific gravity,
2,003
Research residence,
879,899
of fuel gas,
454
Residences,
Specific heat,
3,693
air distribution in,
317
mean, of water vapor,
3
humidification of,
252,496
of water,
26
oil burners for,
462
Specific humidity,
8
conversion burners.
473
Specific volume,
3,698
stokers for,
458
of saturated steam,
m
718
ALPHABETICAL
INDEX TO TECHNICAL DATA SECTION
Page
Storage,
Page
Split system,
694
of hot water,
617,671
air conditioning equipment,
automatic control of,
229, 319
244
temperatures and humidities for,
Storm sash,
68
122
central fan,
359
Sub-atmospheric systems, 514, 520,
529,539,547
Spray,
Suction,
booths for painting,
351
static, in exhaust systems,
347
cooling,
unloaders,
211
ponds,
190, 192
Sulphur dioxide in air,
09
efficiency of,
191
Summer,
towers,
191, 192
care of heating boilers,
419
distribution of,
73
comfort zone,
43,46,48
generation of,
type of central station system,
73
156
conditioning, apparatus for,
desirable indoor conditions in,
155, 159
48,50
water coolers,
177
temperatures,
147
Square foot of heating surface,
604
wind velocities and directions,
147
Stack, stacks,
81,389
Sun
effect,
7S
diurnal movement of,
148
height,
694
effect,
60
size of,
system with registers,
wall,
83,392,401
SI
392
effect on heating requirements,
factor of cooling load,
517
152
Stairways,
127
cooling,
156
Standards,
air conditioning,
A.S.H.V.E, codes and standards.
33,48
48, 704
equipment,
air conditioning,
162
156
162
commercial regain,
70
extended,
497
for pipe,
for ventilating industrial plants,
581
262
gravity-indirect heating systems,
heating,
499
689, 691
for welding,
f>91
square foot of,
694
Steam,
188, 694
radiant heating,
661
205
secondary ,
466
condensing rates,
flow, Babcock's formula,
heat content of,
as heat source,
494
527
18
670
Symbols,
for drawings,
for heat transmission formulae,
Synthetic air chart,
701
92
694
heating systems,
503, 670
air-vent, 503,
507, 535, 536
T
atmospheric,
511,539,547
classification,
503
Tank, tanks,
condensation return pumps,
518
for domestic water supply,
605
connections, (see Connects
5ns; Fittings')
expansion,
574
corrosion of,
595
flush,
605
design of,
511, 527
Tees, dimensions of,
587
clirt pockets,
district heating,
dripping of,
electric
555
639
555
670
Temperature,
absolute,
of air leaving outlets,
685
159, 364
equivalent length of run,
gravity systems,
one-pipe, 503,
531
503
500, 535, 547
ammonia,
apparatus sensitive to,
for banana ripening,
188
239, 676
71
two-pipe,
507, 536, 547
of barns,
87
with high-pressure steam, 539
mechanical, 503
oriflce, 516, 529, 539, 547
pipe, 527 (see also Pipe)
capacity, 529, 532
sizes, &2S. 532
basic,
body,
changes, effect on human beings,
of chimney gases,
in cities,
of city water.
34, 30, 658
37
428
136, 147, 484
179
pressure drop i»,
sub-atmospheric, 514, 520,
type? of,
vacuum, 513,519,522,
505, 515
529, 539, 547
503
538, 547, 696
commonly specified, *
control of,
of cooling water,
dew-point,
3
243, 465, 672
188
2,251
vapor,
one-pipe,
two-pipe,
water hammer in,
high pressure,
jet apparatus,
meters for,
pressure,
properties of,
requirements of buildings,
saturated, properties of,
savings in use of,
tables,
529, 547
508
508, 537
530
539
204, 675
648
539
22, 670
651
28
645
7, 18, 28
difference,
between floor and ceiling,
desired, determination of,
in stacks and leaders,
dry-bulb,
as index of air distribution,
maximum design,
specified in winter,
for drying lumber,
efject on moisture regain,
efcrect on sound,
effective, 41, 49
A.S.H.V.E. standards,
chart,
134, 494
83
81, 301
1, 9, 49, 688
51
147
132
72
67
, 133, 165, 688
49
40
trap,
underground,
in unit heaters,
039
221
for maximum comfort,
optimum,
scale.
48, 659
43
39, 50
Stokers,
of gas flame,
automatic control of,
247, 383
for greenhouses,
72
design of,
457
in industrial plants,
65, 485
economy of,
mechanical,
type* of,
457
457
408, 457
in industrial processing,
inside, 48
surfaces,
68,70
, 133, 364, 483
860
719
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Temperature (continued)* Page
low, insulation for, 624
of mean interior surface, 660
mean radiant, 657, 660
measurement of, 87, 239, 676
in occupied space, 48, 52, 483
outside, 134, 146, 483
radiation-convection, 663
range of cooling equipment, 189\
records of cities, 136, 147, 484
at registers, 391, 396, 500
room, . 9, 195, 483, 677
sensations, 38
surface,
of man, 658
mean interior, 660
systems for control of, 243, 465, 672
for textile testing, 70
thermo-equivalent conditions, 39
value used in calculations, 124, 364
wet-bulb, 2, 15, 680, 696
average, 189
design, 147, 189
as index of air distribution, 51
maximum, 189
Terminology, 685
Test methods, 675
Textile, textiles,
fibres,
regain of moisture, 65
weaving of, 67
temperatures and humidities for processing, 69
testing, standard atmosphere for, 70
Theaters,
air distribution in, 321
* cooling in, 320
heat sources in, 138
temperatures of, 48, 132
Thermocouples, 676
Thermodynamics, 694
of air conditioning, 1
laws of, 691
Thermo-equivalent conditions, 39
Thermometer,
duct,
globe,
Kata,
mercurial,
recording,
resistance,
Thermometric chart.
Thermopile,
Thermostat, thermostats,
differential,
with gas-fired furnaces,
location of,
with oil burners,
with radiant heaters,
types of,
Tobacco smoke,
Ton of refrigeration.
Ton-day of refrigeration,
Towers, cooling,
atmospheric,
mechanical draft,
natural draft,
Traps,
dust catchers,
return, automatic,
with steam heating systems,
types of,
Tube,
Bourdon,
Pitot,
ihell and tube heat exchanger,
Tuning fork,
Tunnels, for steam pipe,
Turbines, with unit heaters,
677
663
079
676
677
676
40
676
696
9,262
472
243, 247, 383
464, 408
672
81,228,239
52, 212
170, 695
695
174, 179, 187, 190
192
195
192
191
f
266
524
309, 520
521
675
678
177
aoi
643
226
Two-pipe stearn heating systems, . Page
gravity air-vent, 507, 536, 547
down-feed, 508
up-feed, 507
vapor, 508, 537
down-feed, 510
U
Ultra-violet light, 56, 261
Underwriters' loop, 505, 545
Unit air conditioners, 197, 319, 695
accessory apparatus, 198
advantages, 200
classification, 201
costs, initial and operating, 215
design of, 207
functions of, 201
installation of, 213
location of, 206
ratings of, . 214
required capacity of, ^14
types of, 205
uses of, 200
Unit conditioning systems,
197 (set Unit Air Conditioners)
Unit coolers, 219, 695
design of, 234
ratings of, 236
Unit heaters, 219
blow-through type, capacity of, 220
boiler capacity, 224
control of, 243
design of, 219
draw-through type, capacity of, 222
electric, 669
output of, 223
ratings of, 223
types of, 219, 669
used in industry, 226
Unit ventilators, 219, 227
capacity of, 230
control of, 244
design of, 227
ratings of, 231
Unwin pressure drop formula, 640
Up-feed piping systems, 504, 507, 509, 512
Upward system of air distribution, 321
Vacuum pumps, 515
Vacuum refrigeration, 204
Vacuum system of steam heating,
513, 519, 522, f)38, 547, 090
Valve, valves, 592
apparatus which operates, ,241
on boilers, 417, 544
control,
in oil installations, 468
with steam heating systems, 541, 593
with high pressure ateam, 539
operator. Ml
pressure- reducing, 540
ratings of, 5B9
for radiators, 505, 500
roughing-in dimensions, 596
sub-atmospheric system, 515
on traps, 522
types of, 598
for water supply, 604
Vanes, ' 322
Vapor,
mixture with air, 10
pressure, 20
steam heating systems, 508
water, 3, 5, 9, 16, 18
weight of saturated, 10
Vegetables, temperature! for greenhouses, 72
Velocity, 00$
rA.S.H.V.E, ventilation standard*, 49
in ducts of buildings, SB1, 841
in exhaust systems, 347, 353
720
Roll of Membership
AMERICAN SOCIETY of
HEATING and VENTILATING ENGINEERS
1935
Contains Lists of Members
Arranged Alphabetically and
Geographically, also Lists of
Officers and Committees, Past
Officers and Local Chapter
Officers
Corrected to January 1, 1935
Published at the Headquarters of the Society
51 Madison Avenue, New York, N* Y.
Officers and Council
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS
51 Madison Ave., New York, N. Y.
1934-35
President C. V. HAYNES
First Vice-President JOHN Ho WATT
Second Vice-President , _ ,.G. L. LARSON
Treasurer D. S, BOYDEN
Secretary , A. V. HUTCHINSON
Council
C. V. HAYNES, Chairman
JOHN Ho WATT, Vice-Chairman
One Year Two Years Three Years
ALBERT BUENC.KR R. H. CARPENTER M, C. BEMAN
F. E. GlESECKE J. D, CASSELt E. H, GURNEY
W, T. JONES F. C. MC!NTOSU 0. W. OTT
J. F. MclNTiRE L. W. MOON W. A. RUSSELL
W. E. STARK
Committees of the Council
Executive: " John Howutt, Chairman; J. D* Cassell, E. H. Gurney.
Finance: R» H. Carpenter, Chairman; F. C. Mclntosh, J, F. Mclntire.
Meetings; W. E, Stark, Chairman; F. E. Giesecke, L. W, Moon.
Membership: F. C, Mclntosh, Chairman; Albert Buenger, W, A. Russell,
Advisory Council
W, T, Jones, Chairman; Homer Addams, R, P. Bolton, W, H. Carrier, S. E, Dibble,
W, H. Driicoll, H. P., Gant, John F, Hale, L. A, Harding, H, M, Hart, E. Vernon
Hill, J. D, Hoffman, S, A. Jellett, D* D, Kimball, S. R. Lewis, Thornton Lewis,
J, I. Lyle, J. R, McColl, D. M, Quay, C L, Riley, F, B, Rowley, F. R. Still and A, C
Willard.
Cooperating Committees
A»S»H.V,E. representative on National Research Council: Prof, F, E, Giesecke (3 years).
a
Special Committees
Committee on Admission and Advancement: A. J. Offner, Chairman (two years}; J. G.
Eadie (one year), and E. N. Sanbern (three years).
Publication Committee: W. M. Sawdon, Chairman; A. P. Kratz and M. C. Beman.
Committee on Constitution and By-Laws: Thornton Lewis, Chairman; W. T. Jones and
O. W. Ott.
Guide Publication Committee: W. L. Fleisher, Chairman; John Howatt, G. L. Larson,
S. R. Lewis, E. N. McDonnell, W. M. Sawdon and J. H. Walker. J. L. Blackshaw,
technical assistant.
Committee on Ventilation Standards: W. H. Driscoll, Chairman,- J, J. Aeberly, L. A.
Harding, D. D. Kiraball, J. R. McColl, C. L. Riley, W. A. Rowe, Perry West and
A. C. Willard,
Committee on Code for Testing and Rating Condensation and Vacuum Pumps: John
Howatt, Chairman; W. H. Driscoll, L. A. Harding and F. J. Linsenmcyer.
Committee on Code for Testing and Rating Connectors: R. N. Trane, Chairman; E. H,
Beling, R. F. Connell, M. Dillman, W. Ewald, J. H. Holbrook, Hugo Hutzel,
A. P. Kratz, M. G. Steele and O, G. Wendel.
Committees— 1934
Nominating Committee for 1934
Chapters
Cincinnati
Cleveland
Illinois
Kansas City
Massachusetts
Michigan
Western Michigan
Minnesota
New York
Western New York
Ontario
Pacific Northwest
Philadelphia
Pittsburgh
St. Louis
Southern California
Wisconsin
Representative
J. J. BRAUN
C. F. EVELETH
J. J. AEBERLY
W. A, RtJSSELL
J. F. TUTTLE
W. G. BOALES
S. H. DOWNS
N. D. ADAMS
H. W. FIELDER
D. J. MAHONEY
H. S, MOORE
A. L, POLLARD
W. R, EICHBERG
F. C. MclNTOSH
R. J, TENKONOHY
L. H. POLDERMAN
E. A. JONES
Alternate
H, E. SPROULL
F. A, KITCHEN
J, J. HAYES
E. K. CAMPBELL
W. F. GILLXNG
TOM BROWN
J, H. VAN ALSBURG
C, E. LEWIS
V. J. Cuca
J, J. YAGER
F. E. ELLIS
LINCOLN BOUILLON
M. F. BLANKIN
F, C. H00GHTEN
R. L. GlFFORJD
ERNEST SZEKELY
Committee on Research
JOHN HOWATT, Chairman
F. E. GIESECKE, Vice- Chair man
DR. A. C. WILLARD, Technical Adviser
F. C. HOUGHTEN, Director
O. P. HOOD, Ex-Officio Member
One Year Two Years Three Years
D. E. FRENCH ALBERT BUENGER C. A. BOOTH
F. E. GIESECKE S. H. DOWNS E. K. CAMPBELL
L. A. HARDING H. N. KITCHELL JOHN HOWATT
A. P. KRATZ H. R. LINN A. J. NESBITT
G. L. LARSON PERRY WEST J. H. WALKER '
Executive Committee Finance Committee
JOHN HOWATT, Chairman A. J. NESBITT, Chairman
F. E. GIESECKE H. R. LINN N. D. ADAMS G, L. LARSON
E. C. EVANS J. H. WALKER
Technical Advisory Committees, 1934-1935
Air Conditions and Their Relation to Living Comfort: C. P. Yaglou, Chairman; J. J.
Aeberly, W, L. Fleisher, D. E. French, Dr. R. R. Sayersand Dr. C.-E. A. Winslow.
Air Conditioning in Treatment of Diseases: Dr. E. V. Hill, Chairman; N. D. Adams,
J. J. Aeberly, Margaret Ingels, H. R. Linn and E. L. Stammer.
Atmospheric Dust and Air Cleaning Devices (Including Dust and Smoke): H. C. Murphy,
Chairman; J. J. Bloomfield, M. I. Dorfan, Philip Drinker, Dr. Leonard Greenburg,
S. R. Lewis, T. W. Pangborn, F, B. Rowley and Games Slayter.
Correlating Thermal Research: R, M. Conner, Chairman; D. S. Boyden, J. C. Fitts,
H. T. Richardson and Perry West.
Corrosion: J. H. Walker, Chairman; H. F. Bain, E. L. Chappell, W. H. Driscoll and
R. R. Seeber.
Direct and Indirect Radiation with Gravity Air Circulation: H. F. Hutzel, Chairman;
A. P. Kratz, H. R. Linn, J. F. Mclntire, J. P. Magos, T. A. Novotney, R. N. Trane
and G. L. Tuve.
Gas Heating Equipment: W. E. Stark, Chairman; Robert Harper, E. A, Jones, Thomson
King, J . F. Mclntire, E. L, Tornquist and H, L, Whitelaw.
Heat Requirements of Buildings: D. S. Boyden, Chairman; P. D. Close, W. H. Driscoll,
IL M. Hart, P, E. Holcombe, V. W. Hunter, E. C. Rack, F. B. Rowley, R. J. J.
Tennant and J, H- Walker.
Heat Transfer of Finned Tubes with Forced Air Circulation: F. B. Rowley, Chairman;
H. F. Bain, H. F, Hutzel, W. G. King, A. P. Kratz, E, J. Lindseth, L. P. Saunders,
G, L. Tuve and W. E, Stark.
Minimum Temperature and Method of Introduction of Cooling Air in Classrooms: Perry
West Chairman; J, D. Cassell, S. R. Lewis, J, R. McColl, A. J, Nesbitt, G, E, Otis
and C.-E, A, Winslow,
Oil Burning Devices: H, F, Tapp, Chairman; Elliott Harrington, F. B. Howell, J, H.
Mcllvaine, L. E. Seeley and T, H. Smoot.
Pipe and Tubing (Sites) Carrying Low Pressure Steam or Hot Water: S. R. Lewis,
Chairman;], C. Fitts, F. E. Giesecke, H, M, Hart, C. A. Hill, R. R. Seeber and
W. K. Simpson.
Refrigeration in Relation to Air Treatment: A. P, Kratx, Chairman; E. A, Brandt, John
Everetts, Jr., E. D. Milener, K. W. Miller, E. B. Newill, F, G. Sedgwick and J, H,
Walker.
Sound in Relation to Heating and Ventilation: V. 0. Knudsen," Chairman; Carl Ashley,
C, A. Booth, F. C. Mclntosh, R. F. Norris, J. S. Parkinson, C. H. Randolph, J. P.
Reis and G. T. Stanton.
Ventilation of Garages and Bus Terminals: E» K. Campbell, Chairman; S. H. Downs,
T. M. Dugan, E» C. Evans, F. H. Hecht, H, L, Moore and A. H. Sluss.
Officers of Local Chapters
1934-35
Cleveland
Headquarters, Cleveland, Ohio
Meets: Second Thursday in Alonth
President, M. F, RATHER
2142 East 19th Street
Secretary, E. J. VERMERE
2125 Wyandotte Avenue
Cincinnati
Headquarters, Cincinnati, Ohio
'Meets: Second Tuesday in Month
President, H. N. KITCHELL
4528 Circle Avenue
Secretary, E. B. ROYER
6635 Iris Avenue
Illinois
Headquarters, Chicago
Meets: Second Monday in Month
President, R. E. HATTIS
180 N. Michigan Avenue
Secretary, L, S. R*ES
5614 Blackstone Avenue
Kansas City
Headquarters, Kansas City, Mo.
Meets: Second Monday in Month
President, L. A. STKPHKNSON
409 East 13th Street
Secretary, L. R. CHASE
217 Dwight Building
Massachusetts
Headquarters, Boston
Meets; Second Monday in Month
President, R. S, FRANKLIN
88 Chauncy Street
Secretary. W. A. McPituKsoN
86 Dwinneli Street
West Roxbury, Maaa.
Michigan
Headquarters, Detroit
Meets: First Monday after the 10th of the Month
President, G. D. WINANS
2000 Second Avenue
Secretary, W. f . ARNOLD Y
2847 Grand Riv<?r Avenue
Weatem Michigan
Headquarters, Grand Rapids
Meets; Second Monday in Month
President, S. H, DOWNS
211 Creaton Avenue
Kalamaasoo, Mich,
Secretary* W, G. SCHLICHTINU
11417 W. Lovell Street
Kalamaasoa, Mich,
Minnesota
Headquarters, Minneapolis
Meets; Second Monday in Month
President* C. E. LEWIS
820 Second Avenue. S.
Secretary, R, E* BACKSTEOM
643 S, Snelling Avenue, St. Paul, Minn.
New York
Headquarters, New York
Mt:els: Third Monday in Month
President, H. W. FIEDLER
489 Fifth Avenue
Secretary, T. W. REYNOLDS
100 Pinecrost Dr.,
Hastings-cm-Hudson, N. V.
Western New York
Headquarters, Buffalo
Meets: Second Monday in Month
President, .). J. YAGER
425 Woodbrldfie Avenue
Secretary, P. S. HEDLEY
Curtiss Building
Ontario
Headquarters, Toronto, Canada
Meets; First Monday Every Other Month
President, W. R. BLACKHALL
3£2 Waverly Road
Secretary, H, R, Rcmt
1104 Bay Street
Pacific Northwest
Headquarters, Seattle, Wash.
fleets: Second Tuesday in Month
President, A, L. POLLARD
001 Electric Building
Secretary, S. D, PBTKRHON
473 Colman Building
Philadelphia
Headquarters, Philadelphia, Pu,
Meets: Second Thursday in Month
President, W. P, CULBKRT
2019 Rittcnhouee Street
Secretary, W. R.
4210 Sansom Street
Pittsburgh
Uu&dituartere, Pittsburgh, Pa.
Meets: Second Monday in Month
President, L, B. PITTOCK
421) B Oliver Building *
Secretary, T. K. ROCKWELL
Carnegie Institute of Technology
St. Louis
Headquarters, St, Louis, Mo,
Meek; 'First Wednesday in Month
President, J, W» COOPER
1590 Arcade Building
Secretary, A, L, WALTERS
7284 Richmond Place, Maple wood, Mo*
Southern California
Headquarters, Los Angeles
Meets; Second Tuesday in Month
President, W. K. BARNUM
5051 Santa Fe Avenue
Seertiaryt P. C. SCQFIKLD
748 E, Washington Boulevard
Wisconsin
Headquartera, Milwaukee
Mseh; Third Monday in Month
President, EltKEST SfcEKRLY
1817 South 66th Street
Secretary, G. E, HOCESTISIN
3000 W, Montana Stettt
6
Roll of Membership
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS
1934-35
HONORARY MEMBERS
BALDWIN, WM. J. (1915), New York, N. Y. (Deceased May 7, 1924.)
BILLINGS, DR, J. S. (1896), New York, N. Y. (Deceased March 10, 1913.)
GORMLY, JOHN (Charter Member), Norristown, Pa. (Deceased January 31, 19290
NEWTON, C. W. (Charter Member), Baltimore, Md. (Deceased August 6, 1920.)
HOOD, O. P. (1929), Washington, D. C.
JELLETT, STEWART A. (Charter Member), (Presidential Member), Philadelphia, Pa.
LIST OF MEMBERS IN GOOD STANDING
Arranged Alphabetically— All Grades
(Asterisk indicates authorship of papers)
(M 1923; A 1918; J 1916) indicates, Election as Member 1923; Associate 1918; Junior 1916,
(Pres. 1923) indicates, Elected President in 1923 and is now a Presidential Member. *
ABRAHAM, Leonard (J 1035; S 11)32), 37 S.
Washington St., Tarry town, N. Y.
ABRAMS, Abraham \M 1927; J 1924), Prea,,
Abbey Htg, Co,, Inc., 81 Centre Ave,, and (for
mail), 100 Clove Rd., New Rochelle, N. Y,
ACHESON, Albert R. (M 19X0), Consulting Engn
(for mail), 852 Oatrora Ave,, Syracuse, N. Y.
ADAMS, .Benjamin (M 1919), Dist. Mgr. (for
mail). American Blower Corp., 012 Otia Bldg.
and 3006 W, Coulter St., Queen Lane Manor,
Philadelphia, Pa.
ADAMS, Charles W. (M 1920), Salesman, U, S.
Radiator Corp,, 1405 West llth St., Kansas
City, Mo.
ADAMS, Eugene I. (M 1934), Plant Engr,,
Michigan State College, and (for mail), 115 S.
Pine, Lansing, Mich.
ADAMS, Harold E. (M 1930), Chief Engr. (for
mail), Nash Engineering Co., South Net-walk,
and Merrill Heights, Norwalk, Conn.
ADAMS, Nell D. (M 1929; A 1925: / 1922), Supt,,
Franklin Htg, Station (for mail), 220 Second
Ave, S.W., and 836 Eighth Ave, &W,, Rochester,
Minn,
ADD AM S, Homer (Charts? M&mber; life Mm-
fcr)i tPrtstotnttol Umber), Pres., 1924; 1st Vice-
Pres», 1928; Treas,, 1916-1922; Council, 1915-
1926) , Fre®,, Kewanee Boiler Co., Inc., and
FiUgibbont Boiler Co,, Inc-, 570 Seventh Ave,,
New York, N, Y,
ADLAM, T, Napier (M 1982), Chief Bnnr., Sarco
Co,, Inc., 188 Madison Ave., New York, N. Y,,
and (for mail), 6 Lowell Ave*, West Orange, N. J,
ADtBR, Alpho*x»e A,* (M 1921), Consulting
Bnjr.t 33 Stewart Ave,, Arlington, N. J,
AEBmY, John J,* (if 1928), Chief of DIv. of
Heating, Ventilation and Industrial Sanitation,
Chicago Board of Health, 704 City Hill, and (for
mail), 6821 N. Oak Park Ave., Norwood Park
F, (X, Chicago, HI.
AHEARN, William J. (M 1920), Heating and
Ventilating Engr., 21 Lake Rd., Cochituate,
Mass.
AHLBERG, Henry B. (J 1933), Engr., 7 First
Ave., and (for mail), Chase Brass & Copper Co.,
Waterbury, Conn.
AHLFF, Albert A. (M 1923; A 1918), Chase Brass
& Copper Co., and (for mail), 805 Cook St,
Waterbury, Conn.
AIKEN, Jack F. (S 1935), 312 Walnut St., S.E.,
Minneapolis, Minn,
AKERS, George W. (M 1929), Secy-Treaa. (for
mail), George W. Akers Co., 2847 Grand River
Ave., Detroit, and 424 WllHtts, Birmingham,
Mich.
ALFSEN, Nikolai (M 1933), Alfsen & Gunderson,
P. 0, Box 676, Oslo, and (for mail), Shabekk near
Oslo, Norway.
ALGREN, Axel B.* (U 1930), Inst, Mech, Engrg.,
University of Minnesota, Exp, Engrg. Lab., and
(for mail), 6109-17th Ave. S., Minneapolis, Minn.
ALLAN, Norman J. (J 1934), Asst. to Pres.,
Kansas City Pump Co., 1314 West llth St., and
(for mail), 3661 Madison Ave., Kansas City, Mo.
ALLMAN, Norman S, (S 1934), 8420 Lake Ave.,
Cleveland, Ohio.
ALLSQP, Rowland P. (J 1934), Mech. Engr, (for
mail), Mathers Haldenby, Archta., 96 Bloor St.
W., and 89 Nevill Park Blvd., Toronto, Out.,
Canada.
ALT, Harold L.* (M 1813), Bid* Equip. Engr,,
Gibbs & Hill. Penn Station, New Y4?rk, N, Y.,
and (for null), 18-C Kearay St., Newark, N, J.
AMES, Charles F. (A 1928), Vice-Pres, Ames
Pump Co., Inc., 30 Church St, (for mail), Hotel
Walton, 104 W. 70th St., New York, N. Y*
AMMERitAN, Charles R, (M 1916), Consulting
Engr, (for mail), 7724 Century Bldg., and 8908
GwHord Ave,, Indianapolis. Ind.
AN0EREGG, ft. H, (M 1920), Vice-Pres,, The
' Trane Co., and (for mail), 324 North 24th,
taCwae, wk
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
ANDERSON, G. S. (M 1920), Mgr. (for mail),
American Blower Corp., 429 Shell Bldg., 1008
W. Sixth St., and 4267 Holly Knoll Dr., Los
Angeles, Calif.
ANDERSON, David B. (S 1933), Engrg. Dept.,
Wood Conversion Co., W. 1981 First National
Bank, St. Paul, and (for mail), 70 Seymour Ave.,
Minneapolis, Minn.
ANDERSON, Sigurd H. (5 1935) , 3921 Blooming-
ton Ave., Minneapolis, Minn.
ANDES, William (A 1934), Secy-Treas., The
Andico Co., 565 Stones Levee, and (for mail),
4043 West 103rd St., Cleveland, Ohio.
ANDREWS, George H. (A 1934), Partner, Frank
P. Andrews & Son, and (for mail), 213 Meyer
Ave., New Castle, Pa.
ANGUS, Harry H.* (M 191S), (Council, 1927-
1929), Consulting Engr., 1221 Bay St., and (for
mail), 34 Farnham Ave., Toronto, Ont., Canada.
ANKER, George W. (J 1935; S 1933), Gasoline &
Fuel Oil, Rensslaer, and (for mail), 27 Jeannelte
St., Albany, N. Y.
ANTHES, Lawrence Lee (A 1935), Pres., Im-
perial Iron Corp., Ltd., 30 Jefferson Ave.4 and
(for mail), 64 Jefferson Ave., Toronto, Ont.,
Canada.
ARCHDEACON, Howard K. (J 1935; S 1933), 28
Niles PI,, Yonkers, N. Y.
ARCHER, David M. (M 1934), Sales Repr. (for
mail), Sarco Co., Inc., 143 Federal St., Boston,
and 11 Wolfe St., W. Roxbury, Mass.
ARENBERG, Milton K. (A 1920), Dist. M#r. (for
mail), Ilg Electric Vtg. Co., 182 N. LaSalle St.,
Chicago, and 1033 S. Linden Ave., Highland
1 Park, 111.
ARMSPAGH, Otto W.* (M 1919), Chief Engr.,
Kroeschell Engrg. Co., 2306 N. Knox Ave.,
Chicago, and (for mail), 205 S. Summit Ave.,
Villa Park, 111.
ARMSTRONG, Robert W. (S 1935), 2809 E.
Lake of the Isles Blvd., Minneapolis, Minn.
ARNOLD, Edward Y. (A 1931), Mgr. (for mail),
Plbg. & Htg. Assns., 2324 Hampden Ave., and
1634 Laurel Ave., St. Paul, Minn.
ARNOLD, Robert S. (A 1020; / 1922), Dist.
Mgr., Hi jet Heater Sales, The Herman Nelson
Corp,, 130 South 17th St., Philadelphia, and (for
mail), Wallingford, Pa.
ARNOLD Y, William F. (A 1930), Branch Mgr.
(for mail), 2847 Grand River Ave., Detroit, and
520 St. Uair Ave., Grosse Points Village, Mich.
ARROWSMITH, John O. (M 1934), Plant Engr.
(for mail), Canadian Kodak Co,, Ltd., and 389
Durie St., Toronto, 9, Ont., Canada,
ARTHUR, John M., Jr. (M 1923), Supt, Com-
mercial Light £ Steam Sales (for mail), Kansas
City Power & Light Co,, 1330 Baltimore,
Kansas City, Mo., and 3311 State Ave., Kansas
City, Kans.
ASHLEY, Carlyle M.* (M 1931), Div. of Research
(for mail). Carrier Bngrg, Corp., 750 Fre»
linghuyaen Ave., Newark, and 7 GJrard PI.,
Maplewood, N, J.
ASHLEY, Edward E. (M 1912), Consulting Engr,
(for mail), 10 East 40th St. New York, N, Y.,
and P. O. Box 188, Noroton Heights, Conn.
ASTON, James (M 1019), A, M. Byers Co., 235
Water St., Pittsburgh, Pa.
ATHERTON, G. R. (M 1030), 40 West 40th St.,
New York, N, Y.
ATKINS, Thomas 3. (M 1931), Sales Engr.,
Carrier Engrg. Corp., 12 South 12th St, Phila-
delphia, and (for mail), 119 Kenllworth Rd.,
Merlon, Pa,
ATKINSON, Kenneth B. (J 1930), & Eppirt St,
East Orange, N. J,
AVEKY, tester T (M 1934), Free, (for mail),
Avery Engrg. Co., 2341 CarnegieAve., Cleveland,
and 21149 Colby Rd,, Shaker Heights, Ohio.
AXEMAN, James E. (M 1032; A 1081; J 1925),
Br, Mgr* (for mail), Spencer Heater Co., 1205
Court Square Bldg., and 908 Old Oak Rd,,
Stoneleigh, Baltimore, Md.
B
BACHLER, Leonard J. (M 1918), 304 East 41st
St., New York, N. Y.
BACKSTROM, Russell E.. (A 1931; J 1928), (for
mail), Wood Conversion Co., 1st National Bank
Bldg., and 543 S. Snelling Ave., St. Paul, Minn.
BACKUS, Theodore H. L. (M 1916), Schumacher
& Backus, 200-208 Hill St., Ann Arbor, Mich.
BADGETT, W. Howard* (J 1932), Research
Asst., Texas Engrg. Experiment Station, College
Station, Texas.
BAHNSON, Frederick F.* (M 1917), Vice- Pres.
and Chief Engr. (for mail), The Bahnson Co.,
1001 S. Marshall St., and 28 Cascade Ave.,
Winston Salem, N. C.
BAILEY, Edward P., Jr. (M 1925), Consultant,
Mayfield Rd. at Lee Blvd., and (for mail),
2475 Lee Blvd., Cleveland, Ohio.
BAILEY, W. Mumford (M 1930), Managing
Director, Mumford Bailey & Preston, Ltd., and
Joint Managing Director, British Trane Co,,
Ltd. (for mail), "Newcastle House," Clcrkenwell
Close, London EC1, and "Oldbury Court,"
Dainesway, Thorpe Bay, Essex, England.
BAKER, Howard C* (M 1921), The II. C. Baker
Co., 12S S. St. Clair St., Toledo, Ohio.
BAKER, Irving G. (KI 1921), Mgr. Air Cond.
Div, (for mail), York Ice Machinery Corp., and
004 Linden Ave., York, Pa.
BAKER, Roland H. (M 1928; A 1924), Pres. (for
mail), R, H. Baker Co., Inc., 145 Broadway, and
420 Memorial Dr., Cambridge, Muss.
BALDWIN, William Howard (M 1921), Br.
Mgr. (for mail), C. A. Dunham Co., 2988 1C.
Grand Blvd., and 1022 Virginia Park, Detroit,
Mich.
BALSAM, Charles P. (M 1932), 324 Fourth St.,
Brooklyn, N. Y.
BARBERA, Henry A. (S 1932), 1727 Colden Ave.,
New York, N. Y.
BARBIERI, Patrick J. (S 1933), 2100 Belmont
Ave., New York, N. Y.
BARNES, Walter E. (M 1933), Pres., Barnes &
Jones, Inc., 128 Brookaide Ave., Jamaica Plain,
Boston, and (for mail), 7 Woodlawn Ave..
Wellesley Hills, Mass.
BARNS, Amos A, (M 1933), Owner (for matt),
440 W. State St., Ithaca, N. Y.
BARNUM, Charles R, (3 1935), 1494 Capitol
Ave., St. Paul, Minn. ,
BARNUM, Marvin C. (M 1930,- A 1928), Rm.
1022-1133 Broadway, New York, N. Y.
BARNUM, Willis E., Jr. (M 1933; A 1933; J 1930)
Sales Engr., York Ice Machinery Co., 5061 Santa
Fe Ave,, Los Angeles, and (for mail), 249(1
Poplar PL, Huntington Park, Calif.
BARR, Geor&e W. (M 1905). 0!at. M«r,, Aeroan
Corp., Land Title Bldg,, Philadelphia, and (for
mail), Woods End, Villanova, Pa.
BARRY, James G., Jr. (M 1933), VJce-Pres. (for
mail), 'Elliott & Barry Engr«, Co., 4060 W. Pine
Blvd., and 5051 Queens Ave,, St. Louis, Mo.
BARRY, Patrick L (M 1920), M. Barry, Ltd., 4
Marlboro St., Cork, Ireland.
BARTH, Herbert fe. (M 1920L Sales Mgr.,
American Blower Corp., 6000 Russell St.,
Detroit, Mich,
BARTLETT, Amos C. (M 1919), Diat, Mgr. (for
mail), B, F. Sturtevant Co,, 89 Broad St.,
Boston, and 30 HoIlingBworth Ave., Braintree,
Mass.
BARTLETT, C. Edwin (M 1922), Pnss., Bartlett
& Co., Inc. (for malt), 1938 Market St., and Sill
W. Coulter St., Philadelphia, Fa.
BASTEDO, Albert E, (M 1919), Vice-Pres-Treaa-
Mgr. (for mall), Burnham Boiler Corp.* Irving-
ton-on-Hudson, and Burnslde Dr., Hastings-on-
Hudson, N. Y.
BAUM, Albert L. (M 1916), Member of Firm (for
mail), Jaros Baum & Ballet, 415 Lexington Ave»»
and 001 West 113th St., New York, N. Y»
BAUMGAR0NEH, Carroll Mile* (M 1028), $r.
Mar. (for mall), U. S. Radiator Corp., S254 N,
Kirbourn Ave.» Chicago, and 602 Michigan Ave.,
Evanston, 111.
ROLL OF MEMBERSHIP
BAYSE, Harry V. (M 1923), American Furnace
Co., 2725 Morgan St., St. Louis, Mo.
BEARD, Earl L. (S 1934), 736 East 13th St.,
Oklahoma City, Okla.
BEAURRIENNE, Auguste* (M 1912), Consulting
Engr., 25 Rue des Marguettes, Paris, France.
BEAVERS, George R. (M 1929), Chief Engr.,
Canadian Blower & Forge Co., Ltd., Woodside
Ave., and (for mail), 168 Samuel St., Kitchener,
Ont., Canada.
BEEBE, Frederick E. W. (A 1915), Johnson
Service Co., 28 East 29th St., New York, N. Y.
BEGGS, William E. (M 1927), Pres., W. E. Beggs
Co., 907 Lloyd Bldg., and (for mail), 3639
Palatine Ave., Seattle, Wash.
BEIGHEL, Howard Atlee (A 1927), Sales Repr.
(for mail), The Herman Nelson Corp., 503
Columbia Bank Bldg., Pittsburgh, and 207
Puritan Rd., Rosslyn Farms, Carnegie, Pa.
BEITZELL, Albert E. (A 1933; J 1930), Mgr.,
Westinghouse Air Cond. Div. of Wm. E. Kings-
well, Inc., 1214-24th St., and (for mail), 1339
Girard St. N.W., Washington, D.C.
BELING, Earl H. (A 1930; J 1925), 2428-13th
St., Moline, 111.
BELL, E. Floyd (M 1933), (for mail), 619 Foshay
Tower, and 2605 Fremont Ave. S., Minneapolis,
Minn.
BEMAN, Myron C. (M 1926), (Council, 1934),
Consulting Engr. (for mail), Beman & Candee,
374 Delaware Ave., and 699 Richmond Ave.,
Buffalo, N. Y.
BENNETT, Edwin A. (J 1929), Sales Engr. (for
mail), American Blower Corp., 401 Broadway,
New York, and 45 Pondfield Rd. W., Bronxville,
N. Y.
BENNITT, George E. (M 1918), Consolidated
Gas Co. of New York, 4 Irving PI., New York,
N. Y.
BENOIST, LeRoy L. (M 1934), Mgr. (for mail),
Benoist Bros. Hardware & Sup., 117 South 10th
St., and 1500 Main St., Mt. Vernon, 111.
SENSE, William M. (S 1934), Engr., Institute
of Tlaermal Research (for mail), American
Radiator Co,, 675 Bronx River Rd., Yonkers,
and 340 Hayward Ave., Mt. Vernon, N. Y.
BENTZ> Harry (M 1915), 18 Holland Terrace,
Montclair, N. J.
BERCHTOLD, Edward W. (M 1927; A 1925) ,
Rate Engr, (for mail), Boston Consolidated Gaa
Co., 100 Arlington St., Boston, and 20 Randolph
St., S. Weymouth, Mass.
BERGHOEFER, Victor A. (/ 1926), Vice-Pres.,
Sterling Engrg. Co., 3738 N. Holton, and (for
mail), 4129 North 20th St,, Milwaukee, Wis.
BERMAN, Louis K. (M 1008), Pres. (for mail),
Raisler Heating & Sprinker Cos., 129 Amsterdam
Ave., and 101 Central Park West, New York,
N. Y.
BERMEL, Alfred H. (A 1933; J 1928), 16 Pershing
PL, North Arlington, N. J.
BERNHAR0, Georfte (A 1929), Pres., Bernhard
Engrg. Corp,, 101 Park Ave., New York, and
(for mail), 18 Liamore Rd., Lawrence, L, L, N. Y.
BERNSTROM, Bert (M 1930), Engr., 132 West
04th St., New York, N. Y,
BEST, Milliard W, (A 1933) f Pres, (for mail),
KoMeetric Underfeed Stoker Co., Ltd,, 245
Kenilworth Ave. S,, and 1750 King St. K.,
Hamilton, Ont, Canada.
BETLBM, Henrietta T, (J 1984), (for mall),
Betlem Heating Co., 1026 Eaat Ave., and 1293
Park Ave., Rochester, N. Y,
BETTS, Howard M, (U 1927), Senior Mech,
Kngr., Htg, & Vtg. (for mail), Dept. of Bldp,,
City of Minneapolis, 213 City Hall, and 4923
Russell Ave. S,, Minneapolis, Minn.
BETZ, Harry D. (M 1928), Pres. (for mail), Betz
Unit Air Cooler Co., 6 W. Ninth St., and 4210
Mercer, Kansas City, Mo,
BILYEU, William F, (M 1927), Eastern Div.
Mgr, (for mail), The Trane Co,, 1109 Chanln
Bldg., New York, and Gibson Apt., Flushing,
L* I* N. Y..
BINDER, Charles G. (M 1920), Mgr. Htg. Dept.,
Warren Webster & Co., 17th and Federal Sts.,
Camden, and (for mail), 115 Oak Terrace,
Merchantville, N. J.
BINFORD, Wilmer M. (J 1930), Mgr. Contract
Dept., S. Div. (for mail), 2120 East 25th St., and
6215 San Vicente Blvd., Los Angeles, Calif.
BIRD, Charles (A 1934), Treas. and Gen. Mgr.
(for mail), The Doermann-Roehrer Co., 450-56
E. Pearl St., and 3026 Beaver Ave., Cincinnati,
Ohio.
BIRRELL, Allan L. (A 1925), Consulting Engr.,
372 Bay St., Toronto 2, and (for mail), 93
Kingsway, Toronto 9, Canada.
BISCH, Bernard J. (M 1931), Engr., St. Mary of
The Woods College, St. Mary of The Woods, Ind.
BISHOP, Charles R. (Life Member; M 1901) ,413
Locust St., Lockport, N. Y.
BISHOP, Frederick R. (M 1921), 8011 Dexter
Blvd., Detroit, Mich.
BJERKEN, Maurice H. (A 1927), Dist. Repr. (for
mail), Hoffman Specialty Co., 533 S. Seventh St.,
and 4952-17th Ave. S., Minneapolis, Minn.
BLACK, Edgar N., 3rd (M 1922), Philadelphia
Mgr., Fitzgibbons Boiler Co., Inc., 814 Land
Title Bldg., Philadelphia, and (for mail). 111
Woodside Rd., Haverford, Montgomery Co., Pa.
BLACK, F. C. (M 1919), Pres. (for mail), F. C.
Black Co., 622 W, Randolph St., and 4535 N.
Ashland Ave., Chicago, 111.
BLACK, Harry G. (M 1917), Prop, (for mail),
P. Gormly Co., 155 North 10th St., and 927
North 65th St. Philadelphia, Pa.
BLACK, William B. (J 1932), Bryant Heater Co.,
135 Seward Ave., Bradford, Pa.
BLACKBURN, Edwin C., Jr. (M 1929), Con-
sulting Engr., 12 Clermont Ave., Hempstead,
L. L, N. Y.
BLACKBALL, Wilmot R. (M 1922), Partner,
McKellar & Blackball, 1104 Bay St., and (for
mail), 332 Waverly Rd., Toronto, Canada.
BLACKMAN, Alfred O. (M 1911), Consulting
Engr. (for mail), 145 West 45th St., and 149
West 12th St., New York, N. Y.
BLACKMORE, F. H. (M 1923), Mgr. Operating
Dept. (for mail), U. S. Radiator Corp., Box 686,
Detroit, and 515 Tooting Lane, Birmingham,
Mich.
BLACKMORE, Georfce C. (Charter Member;
Life Member}, Pres., Automatic Gas Steam
Radiator Co., 301 Brushton Ave., Pittsburgh, Pa.
BLACKMORE, J. J.* (Charter Member: Life
Member), 32 West 40th St., New York, N, Y/
BLACKMORE, James S, (J 1931), Sales Engr.,
H. A. Thrush & Co., Peru, Ind., and (for mail),
4315 Maple Ave,, Edgewood, Pittsburgh, Pa.
BLACKSHAW, J. L,* (J 1929), 68 Plaza St.,
Brooklyn, N. Y.
BLANDmG, George H. (M 1919), 800 N.
Lombard Ave., Oak Park, 111.
BLANKIN, Merrill F. (M 1927; A 1926; J 1919)
Pres. (for mail), Haynes Selling Co., Inc., 1518
Fairmount Ave,, and 3328 W. Penn St., Phila-
delphia, Pa.
BLISS, Georft© L. (A 1933), Engr. and Sales, (for
mail), Allia-Chalmers Mfg. Co., 1410 Waldheim
Bldg., llth and Main, and 7041 Brooklyn Ave.,
Kansas City, Mo.
BOALES, William G. (A 1923), Mfr. Agt (for
mail), 6537 Hamilton Ave., Detroit, and 195
McMillan Rd., Grosse Points Farms, Mich,
BOCK, Bernard A. (A 1929; / 1927), Engrg.
Draftsman, 425 Beech St., Arlington, N, J.
BOCK, L I. (A 1934), Sales Engr. (for mail),-
Carrier Engrg. Corp,, 2022 Bryan St., and 2500
South Blvd., Dallas, Texas.
BODDINGTON, William P. (M 1927), Mgr. (for
mail), The Canadian Powers Regulator Co.,
Ltd., 106 Lombard St., and 280 Clendenan Ave.»
Toronto, Ont,, Canada.
BODINGBR, J. H. (M 1931), Prea. (for mail),
Bodinger & Co,, Inc., 439 West 38th St,» New
York, and 1429 East 19th St., Brooklyn, N. Y,
BOGATY, Hermann S. (M 1921), 5230 North
l»th St., Philadelphia, Pa,
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
BOLSINGER, Raymon C. (M 1916), Mgr. (for
mail), Automatic Florzone Htg. Co., 319 E. Main
St., Norristown, Pa., and 238 E. Madison Ave.,
Collingswood, N. J.
BOLTE, E, Endicott (A 1929), Salesman,
National Radiator Corp., 1111 East 83rd St., and
(for mail), 6516 Kenwood Ave., Chicago, 111.
BOLTON, Reginald Pelham* (Life Member;
M 1897), (Presidential Member}, (Pros., 1911;
1st Vice-Pres, 1905-1910; 2nd Vice-Pres., 1903;
Board of Governors, 1901, 1905, 1910, 1911,
1912, 1913), The R. P. Bolton Co., 116 East 19th
St., New York, N. Y.
BOLZ, Harold A. (J 1934), Asst. Instructor,
Mech. Bngrg. Dept., Case School of Applied
Science, University Circle, Cleveland, and (for
mail), 3558 East 159th St., Shaker Heights, Ohio.
BOND, Horace A. (M 1930), Mgr., Warren
Webster Co., 91 State St., and (for mail), 12
Ramsey PI., Albany, N. Y.
BOOTH, C. A. (M 1917), Vice-Pres. (for mail),
Buffalo Forge Co., 490 Broadway, and 142
Summit Ave., Buffalo, N. Y.
BOOTH, Harry N. (M 1924; A 1917), Vice-Pres.
Sales Dept. (for mail), U. S. Radiator Corp.,
Room 1056 1st National Bank Bldg., and 688
Taylor Ave., Detroit, Mich.
BORLING, John R. (A 1934), Engr.-Custodian
Board of Education, 6520 S. Wood St., and (for
mail), 6818 Normal Blvd., Chicago, 111.
BORNEMANN, Walter A. (M 1924; J 1923),
Sales Engr. (for mail), Carrier En«r. Corp., 12
South 12th St., Philadelphia, and 123 W.
Wharton Ave., Glenside, Pa.
BORUCH, Edwin R. (A 1935), Sales Engr, (for
mail), Dallas Power & Light Co., 1506 Com-
merce, and 835 N. Bishop, Dallas, Texas.
BOUCHERLE, Henry N. (M 1934), Secy, (for
mail), The Scholl-Chofrln Co., Mahoning Ave.
and Ho&ue St., and 3412 Hudson Ave., Youngs-
town, Ohio.
BOUEY, An&us J. (J 1930), Sales Engr, (for mail),
B. F. Sturtevant Co., 553 Monadnock Bldg.,
and 4810 Fulton St., San Francisco, Calif.
BOUILLON, Lincoln (M 1933), Consulting Engr.,
1411 Fourth Ave, Bldg,, and (for mail), 4186-
42nd Ave. N.E., Seattle Wash.
BOWERS, Arthur F. (A 1910), Pres., Industrial
Htg. & Engrg, Co., 828 N. Broadway, Milwaukee,
Wis.
BOWERS, Ross C. (A 1932), Br. Mgr. (for mail),
Minneapolis-Honeywell Regulator Co., 335 W.
North Ave., and 3773 North 52ncl St., Mil-
waukee, Wis,
BOWLES, Potter (A 1928), Pres. (for mail),
Hoffman Specialty Co., Inc., 500 Fifth Ave.,
Room 3324, New York, and 078 Ely Ave.,
Pelham Manor, N. Y.
BOWMAN, James W. (S 1934), 210 S, Saute He,
Norman, Okla.
BOYDEN, Davis S.* (M 1900), (Council, 1930-34;
Treaa., 1983-34), Stint., Steam Htg, Service
Dept, (for mail), Etlison Electric Illuminating
Co. of Boston, 30 Boylaton St., Boston, and 1406
Commonwealth Ave,, Brighton, Mass.
BOYKER, Robert Owen (J 1935), Partner (for
mall), Mac Boyker & Son, and 102 Kennebeck
Ave.» Kent, Wash,
BRAATZ, Chester Johnson* (M 1930), Ensrn
Temp. Control, Barber-Colman Co,, and (for
mail), 718 King St., Rockford, 111,
BRABBLE, Dr. Charles W.* (M 1925), Dir.t
Institute of Thermal Research (for mail),
American Radiator Co., 07U Bronx River Rd.,
Yonkera, and Weatchester Park, 50 Lincoln
Ave., Tuckahoe, N, Y.
BRACKEN, John Henry (M 1927) » Mgr.,
Industrial Uses Dept. (for mail), The Cdotftx
Co., 919 N, Michigan Ave,, Chicago, III
BRADFIELD, William W, (M 10263, Consulting
Engr. (for mail), i)01 Michigan Trust Bldg,, and
18& Franklin St, S,B,, Grand Rapids, Mich.
BRADLEY, Eugene I*. (M 1900), Fres. (for mail),
Hester-Bradley Co., 2835 Washington Ave.,
and G98# Penning Ave., St. Louis, Mo.
BRAEMER, William G. R. (M 1915), (for mail),
Wm. G. R. Braemer & Josiah H, Smith, Engrs,
Room 1265 Commercial Trust Bldg., Phila-
delphia, Pa., and 223 Chestnut St., Haddon-
field, N. J.
BRANDI, O. H. (M 1930), Lufttechnische Gesell-
schaft m. b. H., Berlin W. 50, Nurnbergerstr.
53/55, and (for mail), Landoltwcg 21, Berlin,
Dahlcm, Germany,
BRANDT, Ernst H., Jr. (M 1928), Pres., Reliance
Engrg. Co., Inc., 515 N. Church St., and (for
mail), P. O. Box 1292, Charlotte, N. C,
BRAUER, Roy (M 1920), Prop, (for mail),
Ventilating Equip. Co., 1101 Bessemer Bldg.,
Pittsburgh, and R. F. D. No. 1, Hillcrest, Library,
Pa.
BRAUN, John J. (M 1932), Factory Mgr., The
U. S. Playing Card Co., Norwood Station, Cincin-
nati, and (for mail), 4305 Floral Ave., Norwood,
Ohio.
BRAUN, Louis T. (M 1021), Executive Secy, (for
mail), Chicago Master Stcamfittcra Assn., 228
N. LaSalle St., and 1548 Pratt Blvd., Chicago,
BRECKENRIDGE, L. P.* (Life Member,- M 1920), '
The Brackens, N. Ferrisburg, Vt.
BRE0ESEN, Bernhard P. (A 1931), 3119 Knox
Ave. N., Minneapolis, Minn.
BREITENBACH, George C. (A/ 1933; A 1933;
J 1928), Sales Engr., The Trane Co., 200G
Chestnut St., Philadelphia, and 300 Essex Ave.,
Apt. 203 A, Narberth, Pa.
BRENEMAN, Robert B. (A 1931; J 1927), Sales
Engr. (for mail), Armstrong Cork & Insulation
Co., 232 W. Seventh St., and 1557 Addingham
PI., Cincinnati, Ohio.
BRENNAN, John W. (M 1935; A 1934), Salesman
(for mail), American Blower Corp., Ilofmarm
Bids., and 594-1- Yorkshire, Detroit, Mich,
BRIDE, William T. (M 1928; A 1928: J 1025),
Supt., Enurg. (for mail), P. O. Box 777, Lawrence,
and 50 High St., Mcthucn, Mass.
BRIGHAM, Frederick H. (M 1930) , Sales En«rM
G. H. Gleason & Co,, 25 Huntington Ave,,
Boston, and (for mail), 80 Bedford St., Lexing-
ton, Mass,
BRINKER, Harry A. (Af 193-1), Member of Firm,
Wilson- Brinker Co., 412 Pythian Bldg., and (for
mail), 524 Village St., Kalamausoo, Mich.
BRINTON, Joseph Ward (M 1920), Dist, Mgr.
(for ranil), American Blower Corp., 1003 Statler
Bldg,, Boston, and 42 Gleason St., West Mcdford,
Mass,
BRISSBTTB, Leo A. (M 1030), Treaa. (for mail),
Trask Ht«. Co,, 4 Merriniac St., Boston, and 108
Florence St., Melrose, Mass.
BRODERICK, Edwin L.* (M 1033), Research
Aast, in Mech, Kn«r, (for mail), University of
Illinois, 210 M, E, Lab,, and 1108 W. Stoughton
St., Urbana, 111.
BRONSON, Carlos E.* (M 1919), M«ch, Engr.
(for mail), Kewan«e Boiler Carp,, and 811
McKinley Ave., Kewanee, Ul.
BROO&S, Frank W. (S 1931), (for mail), 2111
Abington Rd., Cleveland, and 93S N, Broadway,
Dayton, Ohio,
BROOM, Benjamin A. (M 1914), Sales Promo-
tion Engr., Weil McLain Co., Ml W. Lake St.,
and (for mail), 1644 Sherwln Ave., Chicago, 111,
BROWN, Alfred F, (M 1927), Vice-Fres, (for
mail), Reynolds Corp,, 809 N, LaSaiJe St.,
Chicago, and 551 Hill Terrace, WinnHfca, 111,
BROWN, Aubrey L* (M 1028), Prof, of Htg, and
Vt«, (for mail), Ohio State University, and I8»
Richards Rd,, Columbus, Ohio,
BROWN, Poufcott* (M 1986), VicenFres. tfor
mail), Gray & Dudley Co., W Third Am N.,
, .,
P, O, Bosc 7232, and 2314 West Ead
ville, Tenn,
e., Naeh*
BROWN, Morrlft (J 1028), Htg. Eagr. (for mail),
Brown Bros., 340 Talbot Ave., and 00© Park St.,
Dorchester, Maaa,
BROWN, Ronald F. (S 1033), ©6 Mitchell Av«.»
Blnghamton, N. Y,
10
ROLL OF MEMBERSHIP
BROWN, Tom (M 1930), Gen. Mgr. (for mail),
Autovent Fan & Blower Co., 1805 N. Kostner
Ave., and 5826 Lake St., Chicago, 111.
BROWN, William A. (M 1930), 2523-14th St.
N.W., Washington, D. C
BROWN, William H. (A 1923), Mgr. (for mail),
Brown Bros., 3310 W. North Ave., and 3015
North 22nd St., Milwaukee, Wis.
BROWN, W. Maynard (A 1930), Warren Webster
& Co., 17th and Federal Sts., Camden, N. J.
BROWN, W, Murray (J 1935; 5 1930), Draftsman
and Estimator (for mail), William P. Brown, 31
Sanford St., and 7S Randolph St., Springfield,
Mass.
BROWNE, Alfred L. (M 1923), Illinois Engrg.
Co., 3514 Grand Central Terminal, New York,
N. Y., and 253 Highland Rd., South Orange,
N. J.
BRUGKMANN, John C. (J 1935; 5 1932), Sales
Repr., American Radiator Co., 40 West 40th St.,
and (for mail), 2290 Sedgwick Ave., New York,
N. Y.
BRUEGGEMAN, Arthur R. (M 1920), (for mail),
The Erie Engineering Co., 1740 East 12th St.,
Cleveland, and 17220 Aldersyde Dr., Shaker
Heights, Ohio.
BRUNETT, Adrian L. (M 1923), Assoc. Mech.
Engr,, U. S. Supervising Architects Office,
Treasury Dept., Washington, D. .C., and (for
mail), P. O. Box 36,* Rockville, Md.
BRUST, Otto (M 19,30) , (for mail) , Luf ttechnische
Gesellschaft, Prag 1, Revolucni 13 and Veverkova
ul 3 Prag VII Czechoslovakia.
BRYANT, Dr. Alice G. (M 1921), 502 Beacon St.,
Boston, Mass.
BRYANT, Percy J. (M 1915), Chief Engr. (for
mail), Prudential Insurance Co., 783 Broad St.,
Newark, and 754 Belvidere Ave., Westfield, N. J,
BUCK, Lucien (M 1928), Pres. (for mail), Buck
Dryer Corp., P. O. Box 308, Manchester, Conn.
BUCKLEY, Martin B. (A 1930), 824 Grand Ave.,
Kansas City Mo.
BUENGER, Albert* (M 1920; J 1917), (Council,
1934), Mech. Engr. (for mail), C. H. Johnston
Archt., 715 Empire Bank Bldg., and 1606
Stanford Ave., St. Paul, Minn,
BUENSOD, Alfred Charles (M 1918), Sales
Kngr., Carrier Engrg. Corp., Chrysler Bldg., and
(for mail), 1 Fifth Ave., New York, N, Y.
BUFORD, Jack W. (J 1935; 5 1933), 2323 Ash-
land Ave., Walnut Hills, Cincinnati, Ohio.
BULKELEY, Claude A> (M 1923), Chief Engr.
(for mail), Niagara Blower Co., 6 East 45th St.,
and 410 West 68th St., New York, N. Y.
BULL, Alvah Stanley (J 1935; S 1933), 304 West
35th St., Minneapolis, Minn.
BULLEIT, Charles R. (M 1932; A 1932; J 1930),
281-2 Austin Ave., Bvansville, Ind.
BULLOCK;, Howard H. (A 1933), Commercial
Engr, (for mail). General Electric Co., 5201
Santa Fe Ave,, Los Angeles, and 2530 Grand St.,
Walnut Park, Calif.
BULLOCK, Thomas A, (M 1980), Engr. (for
mail)* Densmorc, LeClear & Robbina, 31 St.
James Ave,t Boston, and 89 Fairmont St.,
Arlington » Mass.
BUOT, Antonio V, (S 1036), 2730 Portland Ave,
S,, Minneapolis, Minn,
BUR, Julian R, C. (J 1931), Chief Engr. (for mail).
Bur & Co,, 10 Rue du Chapeau Rouge, and 1
Place Francois, Rude Dijon, France. •
BURBAUM, W. Allen (J 1933), Asst. Br. Mar.,
Rex Cok Inc., 2392 Grand Concourse, New
York, and (for mail), 180 Clinton Ave*, Brooklyn,
N, Y.
BURCH, Laurence A. (M 1934). Mgr, Htg, Div.,
Porfex Radiator Corp,, 415 W, Oklahoma PL,
and (for mall), 421 B. uoyd St, Milwaukee, WJa.
BURKB, James J* (/ 1930), Engr. (Air ConcU),
Carrier Bngri, Corp,, 850 Frellnflhuysen Ave.,
Newark* and (for mall), 720 N. Broad St.,
£li*»b«th, N* J.
BURKft, William J. (A 1934), 1109 S. Cartoon
8L» Tulsa, Old*.
BURNETT, Earle S. (M 1920), Mech. Engr.,
U. S. Bureau of Mines, Arnarillo Helium Plant,
P. O. Box 2025, and (for mail), 4223 West llth
Ave., Amarillo, Texas.
BURNS, Edward J. (M 1923), 4716 Aldrich Ave.
S., Minneapolis, Minn.
BURNS, John R. (J 1935; 5 1933), (for mail), 5035
Forbes St., Pittsburgh, Pa., and 504 N. Main St.,
Wallingford, Conn.
BURNS, Robert (M 1934), Engr. (for mail), Coal
Stoker Sales Co., 500 N. Craig St., and 482
Antenor Ave., Pittsburgh, Pa.
BURRITT, Charles G, (.4 1916), Mgr., Minne-
apolis Office (for mail), Johnson Service Co., 922
Second Ave. S., and Buckingham Hotel, Minne-
apolis, Minn.
BUSHNELL, Carl D. (A 1921), Pres. (for mail),
The Bushnell Machinery Co., 1501 Grant Bldg.,
Pittsburgh, and 94 Pilgrim Rd., Rosslyn Farms,
Carnegie, Pa.
BUTLER, Peter D. (M 1922), Salesman, U. S.
Radiator Corp., 370 Lexington Ave., New York,
N. Y., and (for mail), 127 Edgewater Rd., Grant-
wood, N. J.
BUTT, Roderick E. W. (J 1930), Partner, Crerar,
Butt & Co., 14 Regent St., London S.W.I., and
(for mail), 3 Orme Court, London W2, England.
BUTTS, Robert L. (S 1935), 64th and Norman-
dale Sts,, Minneapolis, Minn.
CALDWELL, Arthur C. (M 1930), Estimator and
Engr., P. Gormly Co., 155 North 10th St., and
(for mail), 550 South 48th St., Philadelphia, Pa.
CALEB, David (M 1923), Engr. (for mail),
Kansas City Power & Light Co., 1330 Baltimore
Ave., and 141 Spruce St., Kansas City, Mo.
CALLAGHAN, Philip F., Jr. (J 1929), Sales
Mgr., D. G. C. Trap & Valve Co., 9 East 46th
St., New York, and (for mail), 3003 Ave. I,
Brooklyn, N, Y.
CALLAHAN, Peter J. (M 1934), Sr. Draftsman,
College City of New York Project, c/0 C. B.
Heweker, Village Hall, Stapleton» and (for mail),
4057 Amboy Rd., Great Kills, Staten Island,
N. Y.
CAMPBELL, Alfred Q., Jr. (J 1933), Sales Mgr.,
E. K. Campbell Cos., and (for mail), 1083
Meriwether Ave., Memphis, Tenn.
CAMPBELL, Everett K.* (M 1920), (Council,
1931-1933), Pres. and Treas. (for mail), E. K.
Campbell Heating Co.. 2445 Charlotte St., and
3717 Harrison Blvd., Kansas City, Mo.
CAMPBELL, E. K,, Jr. (J 1930), Thermidaire
Corp., 2445 Charlotte St., Kansas City, Mo.
CAMPBELL, F. B. (A 1927), (for mail), American
Radiator Co., 40 West 40th St., New York, and
245 Macon St., Brooklyn, N. Y.
CAMPBELL, Robert B. (S 1934), c/o Mra. L.
Winn, 781 Ocean Ave., Brooklyn, N. Y.
CAMPBELL, Thomas F. (M 1928), MmneapoHs-
Honeywell Regulator Co., 1013 Penn Ave.,
Wilklnaburg, Pa.
CANDEE, Bertram C. (M 1933), Partner, Beman
& Candee, 374 Delaware Ave., Buffalo, and (for
mail), 19 Tremont Ave., Kenmore, N. Y.
CANNON, C. Newton (/ 1935; 5 1933), General
Electric Co,, and (for mail), 1104 Wendell Ave.,
Schenectady, N, Y,
CAREY, James A, (M 1928), Carrier Engrg.
Corp., Newark, N. J., and (for mall), Vlllanova,
Pa.
CAREY, Paul C. (M 1930), (for mall), Runyon &
Carey, 33 Fulton St., Newark, and 31 Clare-
mont Dr.i Maplewood, N, J,
CARLE, William E, (U 1926), Pres. (for mail),
Carle- Boehling Co,, Inc., 1641 W, Broad St., and
2220 Floyd Ave»f Richmond, Va*
CARLSON, Everett E. (M 1932$ A 1929), Br*
Mgr, (for mall), The Powers Regulator Co., 1010
lx>uderoian Bldg., and 66$2 Washington Ave.,
St. Louia, Mo.
CARMAN, G«orft© O. (A 1031; J 1928), Lewis
Institute, Chicago, III,
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
CARPENTER, R. H. (M 1921), (Council, 1930-
1934), Mgr., New York Office (for mail), Nash
Engrg. Co., Graybar Bldg., 420 Lexington Aye.,
New York, and 20 Jefferson Ave., White Plains,
N. Y.
CARR, Maurice t. (M 1931), Director (for mail),
Pittsburgh Testing Lab., P. O. Box 1646, and
Webster Hall, Pittsburgh, Pa.
CARRIER, Earl G. (J 1929), Estimating Engr.,
Carrier South Africa (Pty), Ltd., 20 Beresford
House, Simmonds St., Johannesburg, Transvaal,
Union of South Africa.
CARRIER, Willis H.* (M 1913), (Presidential
Member), (Pres., 1931; 1st Vice-Pres., 1930; 2nd
Vice-Pres., 1929; Council, 1923-32), Chairman
of the Board (for mail), Carrier Corp., 850
Frelinghuysen Ave., Newark, and Rensselaer
Rd., Essex Fells, N. J.
CARTER, Doctor (M 1934), Consulting Engr.,
273 Ave. Haig., Shanghai, China.
CARY, Edward B. (M 1935), Vice-Pres., John
Paul Jones, Cary & Miller, Inc., Cleveland, and
(for mail), 3549 Daleford Rd., Shaker Heights,
Ohio.
CASE, Walter G. (A 1930), Tech. Mgr., Ideal
Boilers & Radiators, Ltd., Ideal House Gt., Marl-
borough St., London W.I., and (for mail), 66
The Ridgeway-Kenton, Middlesex, England.
CASEY, Byron L. (M 1921), Sales Engr. (for
mail), Ilg Electric Vtg. Co., 182 N. LaSalle St.,
Chicago, and 515 N. Park Ave., Park Ridge, 111.
CASEY, Huntley F. (M 1931), Sales Repr., P. O.
Box 271, E. Falls Church, Va., and (for mail),
756 E. River St., Anderson, S. C.
CASH, Tidie T. (A 1925), Mgr. (for mail),
Grinnell Co., Inc., 240 Seventh Ave. S., and C17
Kenwood Pkwy., Minneapolis, Minn.
CASPERD, Henry W. H. (J 1930), Engr., Carrier
Engrg. Co., Ltd., 12 Mission Row, Calcutta,
India, and (for mail), 21 Robin Hood Lane,
Sutton, Surrey, England.
CASSELL, John D.* (Life Member; M 1913),
(Council, 1930-34), 2008 Walnut St., Phila-
delphia, Pa.
CHANDLER, Clark W. (J 1935; S 1930), (for
mail), Chandler Co., and 1815 Ridgewood
Terrace, Cedar Rapids, Iowa,
CHAPIN, C. Graham (M 1933), 231 State St., .
New London, Conn.
CHAPPELL, Henry D, (M 1931), Dist, Mgr.,
V-Belt Drive Co., 100 Morgan Bldg., and (for
mail), 8019 Third Ave., Detroit, Mich.
CHARLES, Thomas J. (M 1934), Pres. (for mail),
Metropolitan Air Cond. Corp., 432 Fourth Ave.,
New York, and 175 Marine Ave., Brooklyn,
N. Y.
CHARLET, Louis W. (M 1934), Mgr., New York
Br, (for mail), Kewanee Boiler Corp., 35-37
West 39th St. New York, and 427 JRJch Ave.,
Mt. Vernon, N, Y.
CHARLTON, John Felder (A 1932), Engr.,
Appraiser (for mail), Box 2087, and 1631 N.E.
Fifth St., Ft. Lauderdale, Fla.
CHASE, Chmincey L, (M 1931), Ht£. and Vtg.
Engr., Edward E. Ashley, Cons. Engr., 10 East
40th St., New York, and (for mail), 8829 Ft.
Hamilton Pkwy., Brooklyn, N, Y.
CHASE, L. Richard (J 1931), Br. Mgr. (for mail),
Buffalo Forge Co., &15 Dwight Bldg.* and 4822
Wornall Rd., Kansas City, Mo.
CHEESEMAN, Evans W. (5 1034), Carnegie
last, of Tech., Pittsburgh, Pa.
CHERNE, Realto E» (J 1929), Engr., Carrier
Engrg, Corp.. Chrysler Bldg.. New York. N, Y.,
and for mail), 126 DeHart PI., Etabeth, N. J,
CHERRY, Lester A.* (M 1921), Consulting Engr.
(for mail), Industrial Planning Corp., 271
Delaware Ave., Buffalo, and 155 Euclid Ave.,
Kenmore, Eric Co*. N. Y*
CHERVBN, Victor W. (M 1928; A 1920), Chief
Engr, (for mail), Holland Furnace Co., and 326
Maple Ave., Holland, Mich.
CHESTER, Thomaa^JM 1917}, Consulting Engr.,
949 Chicago Blvd., Detroit, Mich.
CHBSNUTT, N, P. (S 1984), 760 De Barr,
Norman, Okla.
CHEYNEY, Charles C. (.4 1913), Asst. Sales
Mgr. (for mail), Buffalo Forge Co., 490 Broad-
way, and 255 Lincoln Pkwy., Buffalo, N. Y.
CHIPPERFIELD, W. H. (A 1934), Service Engr.,
Walker-Crosweller Co., Ltd., 20 Queen Elizabeth
St., S.E.I., and (for mail), 54 Lankers Dr., N.
Harrow, Middlesex, England.
CHOFFIN, C. C. (M 1919), Pres-Treas. (for mail),
The Scholl-ChoSin Co., Mahoning Ave. and
Hogue St., and 560 Tod Lane, Youngstown,
Ohio.
CHRISTENSON, Harry (A 1931), Supt. of Htg.
(for mail), Hunter Prell Co., 311 Elm St., and 85
Wentworth Ave., Battle Creek, Mich.
CHRISTIAN, Charles W. (Life Member; M 1913),
Mgr. (for mail), Chas. W. Christian Co., P. 0.
Box 292, Charlotte, and 1101 Providence Rd.,
Myers Park, N. C.
CHRISTIE, Alfred Y. (A 1933), Salesman, U. S.
Radiator Corp., 233 Vassar St., Cambridge, and
(for mail), 715 LaGrange St., West Roxbury,
CHRISTMAN, William F. (.4 1932; / 1931), (for
mail), Kroeschell Engrg. Co., 2306 N. Knox Ave,,
and 3912 N. Hoyne Ave., Chicago, 111.
CHURCH, Herbert John (M 1922), Mgr. (for
mail), Darling Brothers, Ltd,, 137 Wellington
St. W., Room 902 Toronto, and 358 Main St. N.,
Weston, Ont., Canada.
CLARE, Fulton Warren (M 1927), Owner (for
mail), Clare & CoM 120 Spring St. N.W., and
935 Plymouth Rd., Atlanta, Ga.
CLARKE, Samuel S. (Life Member; A/ 1900),
Pres. and Mgr. (for mail), S. S. Clarke & Co.,
Ltd., 605 W. Second St., and 003 W. Second St.,
Calgary Alberta, Canada.
CLARKSON, Robert C., Jr. (M 1921), 6050
O verb rook Ave,, Philadelphia, Pa.
CLARKSON, W. B. (Life Member,- M 1919), 251
Broadway, Owatonna, Minn.
CLEGG, Carl (M 1922), Dist. Mgr. (for mail),
American Blower Corp., 311 Mutual Bldg., and
3321 Gillham Rd., Kansas City, Mo.
CLEGG, Robert R. (A 1033), Zone Repr., Owens
Illinois Glass Co., Industrial Div,» Lanclreth
Bldg., and (for mail), 4515 Lindell Blvd., St.
Louis, Mo.
CLODFELTER, John L. (A 1932), Supt. (for
mail), Carolina Sheet Metal Corp., 4210 Sansom
St., Philadelphia, and West Cheater Pike and
Brief Ave., Elizabeth Manor Apt., Upper Darby,
CLOSE, Paul D.* (M 1928), Chief Engr., In-
dustrial Uses Div. (for mail), Celotex Co., 919
N. Michigan Ave., Chicago, and 4622 Grove,
Niles Center, III.
CLOUGH, Leslie (M 1922), Consulting Engr. (for
mail), Box 34 and 203 Pierce Rd., Weymouth,
Mass.
CQCHRAN, Lex H. (M 1934), Dist. Mgr. (for
mail). American Blower Corp., Rialto Bldg., and
130 Camino Del Mar, San Francisco, Calif,
COB, Ralph T. (M 1917), Prop, (for mail), The
R, T. Coe Cos., 400 Reynolds Arcade, and 235
Chile Ave., Rochester, N. Y.
COHAGBN, Chandler C. (M 1919), P» <X Box
2100, Billings, Mont,
COHEN, Nftthan (J 1935 j S 1033), 2305 Loring
PL, New York, N, Y*
COHEN, Philip (M 1932), DM. Mgr, (for mail),
B. F. Sturtevant Co., 407 E. Ohio Gae Bldg.,
Cleveland and 3681 Lynrtfield Rd., Sh&ker
Heights, Ohio,
COLBY, Clyde W. (M 1016), Coatulttaf Bngr*
(for mail). Old School House, South Hadley,
Mass., and 4,0 Rosemere Ave., Rye, N, Y,
COLCLOUGH, O, T. (A 1933), Custodian,
American Leg&tlon. American Government
Bldg., and (for mail), 407 Elgin SL, Ottawa
Canada.
COLE, Edvrtta Q. (M 1931), S82 Lebanon St.,
Mel rose, Mass.
COLE, Grant E. (-4 1025), 489 Kittg St. W,,
Toronto, Ont.» Canada*
ROLL OF MEMBERSHIP
COLEMAN, John B. (M 1920), Chief Engr. (for
mail), Grinnell Co., Inc., 275 W. Exchange St.,
and 237 Cole Ave., Providence, R. I.
COLLAMORE, Ralph (M 1904), (Board of
Governor, 1913), Secy., Smith, Hinchman &
Grylls, 800 Marquette Bldg., and (for mail),
679 Pingree Ave., Detroit, Mich.
COLLIER, William I. (M 1921), W. I. Collier &
Co., 522 Park Ave., Baltimore, Md.
COLLINS, John F. S., Jr. (M 1933), Supervisor
of Steam Utilization (for mail), Alleghany
County Steam Htg. Co., Philadelphia Co. Bldg.,
435 Sixth Ave., and 827 N. Euclid Ave., Pitts-
burgh, Pa.
COMSTOCK, Glen Moore (A 1920), Dist. Repr.
(for mail), L. J. Wing Mfg. Co., 004 Chamber of
Commerce Bldg., Pittsburgh, and 154 College
Ave., Beaver, Pa.
CONNELL, Richard F. (M 1916), Mgr., Capitol
Testing Lab., U. S. Radiator Corp., 1056 First
National Bank Bldg., Detroit, Mich.
CONNER, Raymond M. (M 1931), Director (for
mail), American Gas Assn., 1032 East 62nd St.,
and 271 East 216th St., Cleveland, Ohio.
COOK, Alton B. (S 1934), 533 S. Flood, Norman,
Okla.
COOK, Benjamin F. (M 1920), Consulting Engr.
(for mail), 114 West 10th St. Bldg., Kansas City,
and 1720 Overtoil Ave., Independence, Mo.
COOK, Howard A. (A 1933), Supt., Htg., Vtg.
and Sprinkling (for mail), University Plbg. &
Htg, Co., 3939 University Way, and 1433-33rd
Ave., Seattle, Wash.
COOK, Ralph P. (M 1930), Engr. of Mech.
Equip, (for mail), Eastman Kodak Co., Kodak
Park, and 105 Falleson Rd., Rochester, N. Y.
COOMBE, James (A 1932). Vice-Pres. (for mail),
The Wrn. Powell Co., 2525 Spring Grove Ave.,
and 23«3 Grandin Rd., Cincinnati, Ohio.
COON, Thurlow E. (M 1910), Pres. (for mail),
The Coon-De Visser Co., 2051 W. Lafayette, and
820 Edison Ave.. Detroit, Mich.
COOPER, Frederick IX (A 1930), Sales Engr.,
905 Holdcn Ave., and (for mail), 1746 Longfellow
Ave., Detroit, Mich.
COOPER, John W. (M 1932; A 1925; J 1921),
Repr. (for mail), Buffalo Forge Co,, 1596 Arcade
Bldg., St. Louis, and 312 E. Big Bend Rd.,
Webster Groves, Mo.
COPPERXJD, Edmund R. (/ 1933), Asst. Mgr.
(for mail), Minneapolis Plbg. Co., 1420 Nicollet
Ave., and 4110 Nicollet Ave.» Minneapolis, Minn.
CORNELL, J, Clarence (A 1930), Checker
(Mechanical), 12 South 12th St., and (for mail),
2823 W. Allegheny Ave., Philadelphia, Pa.
CORNWALL, Georfte I, (M 1919), Mgr., Boiler
Dept. (for mail), Hitchings & Co., 701 Spring
St., and 633 Madison Ave., Elizabeth, N. J.
CORRAO, Joseph (J 1933), Engr., C, C, Moore
Co., 450 Mission St., and (for mail), 85«lat
Ave., San Francisco, Calif,
CQRRIGAN, James A. (J 1935; 5 1930), 2501 W.
St. Louis Ave,, St. Louis, Mo.
COWARD, Herbert (M 1921), Carrier Bngrg,
Corp., 004 Washington Bid*., Washington, I>, C.
COX, Harrison F. (A 1930), 243 Carroll St.,
Pateraon, N. J.
COX, William W. Of 1923), (for mail). Heating
Service Co,, 820 Columbia St., and 6232-Slat
Ave. N.B., Seattle, Wash,
CRANSTON, William E., Jr. (M 1931), (Loa
Angeles Board of Governors, 1933-34), Vice-
Pres, (for mail). Thermador Electrical Mfg. Co.,
110 Llewellyn St. LOB Angeles, and 1912 Meri-
dian Ave., South Pasadena, Calif.
CRAWFORD: John H», Jr» (J 1930), 372 High-
land Ave*, Orange, N, J.
CRESSY, Ralph E. (/ 1020), Sales BngrM Hoff-
man Specialty Co., 500 Fifth Ave., New York,
and (tor mail), 408 St, Lawrence Ave,, BuSalo,
GIUQUX, Albert A,* (M 1019), Chief Engr., Htg.
and Vtg, Dept, Buffalo Forge Co., 490 Broad-
way* and (for mail), 250 Blaine Ave,, Buffalo,
N, Y.
CRONE, Charles E., Jr. (M 1922), Secy-Treas.
(for mail), Wendt & Crone Co., 2124 Southport
Ave., and 1320 N. State St., Chicago, 111.
CRONE, Thomas E. (Life Member; M 1920),
Salesman, W. A. Russell & Co., Grand Central
Term. Bldg., and (for mail), 542 West 112th St.,
Apt. 10A, New York, N. Y.
CROSS, Robert E. (A 1931), 95 State St., Spring-
field, Mass.
CUCCI, Victor J. (M 1930), Consulting Engr.,
347 Madison Ave., New York, N. Y.
CULBERT, William P. (A 1929), Secy, (for mail),
Culbert-Whitby Co., Inc., 2019 Rittenhouse St.,
Philadelphia, and 929 Alexander Ave., Drexel
Hill, Pa.
GUMMING, Robert W. (M 1928), Mech. and
Sales Engr., Sarco Co., Inc., 183 Madison Ave.,
New York, and (for mail), 81 Alkamont Ave.,
Scarsdale, N. Y.
CUMMINGS, Carl H. (A 1927; J 1926), Mgr. (for
mail), Industrial Appliance Co. of New England,
250 Stuart St., Boston, and 41 Edgehill Rd.,
Chestnut Hill, Mass.
CUMMINGS, G. J. (M 1923), 2001 Hoover Ave.,
Oakland, Calif.
CUMMINS, George H. (M 1919), Dist. Mgr. (for
mail), Aerofin Corp., 616 United Artist's Bldg.,
and 17376 Wisconsin Ave., Detroit, Mich.
CUNNINGHAM, Thomas M. (M 1931; A 1931;
J 1930), Production Mgr., Carrier Engrg. Corp.,
180 N. Michigan Ave., Chicago, 111.
CURRIER, Charles H. (M 1919), Vice-Pres. (for
mail), Ross Heater & Mfg. Co., Inc., 1407 West
Ave., and Park Lane Apts., 33 Gates Circle,
Buffalo, N. Y.
CURTIS, Herbert F. (A 1934), Berea, Ohio.
CUSHMAN, Lester D. (M 1930), 89 Traincroft
St., Medford, Mass.
CUTLER, Joseph A. (M 1916), (Council, 1917-
1926), Vice-Pres. (for mail), Johnson Service Co.,
1355 Washington Blvd., Chicago, and 649
Hinman Ave., Evanston, 111.
D
DAHLSTROM, Godfrey A. (A 1927), Htg. Sales
Engr., Central Supply Co., 312 S. Third St., and
(for mail), 3721-47th Ave. S., Minneapolis, Minn.
DAILEY, James A. (A 1920), 31-64-30th St.,
Astoria, L. I., N, Y.
DAKJN, Harold W. (J 1934), Asst. Engr,, Wagner
Engrg. Corp., 22 Dunham St., Pittsfield, and (for
mail), 169 Park Ave., Dalton, Mass.
DALLA VALLE, J. M.* (J 1933), Asst. Sanitary
Engr., U. S, Public Health Service, 19th and
Constitution Ave.. Washington, D. C., and (for
mail), 17 Jones Bridge Rd., Chevy Chase, Md.
' DALY, Charles P. (A 1935), Contractor (for mail),
Rantmann Plbg. &"Htg. Co., 115 Jackson St.,
and 2438 Queen Anne. Seattle, Wash.
DALY, Robert E. (M 1931), Executive Dept. (for
mail), American Radiator Co., 40 West 40th St.,
and 12 East 88th St., New York, N. Y.
DAMBLY, A. Ernest (M 1924; J 1921), (for mail),
H. B. Hackett, 901 Architects Bldg., Phila-
delphia, Pa., and Harvey Cedars, N. J.
DANFORTH* N. Lorlnfc (M 1919), John W.
Danforth Co,, 72 Elllcott St. Buffalo, N. Y.
DARBY, Marion H. (J 1930), Sales Engr. (for
mail), Carrier-Brunswick de Mexico, S,A.,
Edincio Cidoaa Deapacho, 101, Uruguay 55,
Mexico, D.F., Mexico.
DARLING, Arthur B. (A 1929), Asst. Sales
Mgr* (for mail). Darling JBros,, Ltd-, 140 Prince
St., and 4216 Dorchester St. WM Montreal, P. Q,,
Canada.
DARLINGTON, Allan P. (M 1930), Salesman
(for mail), American Blower Corp., 2539 Wood-
ward Ave.. and 3605 Devonshire, Detroit, Mich.
DARTS, John A. (M 1919), Kewanee Boiler Co,,
Inc., 570 Seventh Ave., New York, N, Y.
DAUCH, Emll O. (M 1921), Secy-Treas. (for
mall), McCormlck Plbg* Supply Co.. 1075
Bailey Ave., and The Whittler Hotel, Detroit,
Mich.
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
DAVENPORT, R. F. (A 1933), 77 James St. E.,
Brockville, Ont., Canada.
DAVIDSON, L. Clifford (M 1927), Associate Dist.
Mgr. (for mail), Buffalo Forge Co., 220 South
16th St., and 6312 Sherwood Rd., Philadelphia,
Pa.
DAVIDSON, Philip L. (M 1921; J 1921), Asst.
Dist, Mgr. (for mail), Carrier Engrg. Corp. ,'12
South 12th St., Philadelphia, and 14 Radnor
Way, Radnor, Pa.
DA VIES, George William (M 1918), Managing
Dir. (for mail), Htg., Vtg. & Domestic Engrs.,
79 Maclaggan St., Dunedin, and 145 Kenmure
Rd., Mornington, New Zealand.
DAVIS, Arthur C.* (M 1920), Supt. of Main-
tenance, The Port of New York Authority, 111
Eighth Ave., New York, N. Y., and (for mail),
73 Preston St., Ridgefield Park, N. J.
DAVIS, Arthur Folsom (M 1934"), Vice-Pres. (for
mail), The Johnson & Davis Plbg. & Htg. Co.,
2235 Arapahoe St., and 1901 Ivanhoe St.,
Denver, Colo.
DAVIS, Bert C. (JW 1904), (Council, 1917), Pres.
and Treas. (for mail), American Warming &
Ventilating Co., 317-19 Pennsylvania Ave., and
003 W, Church St., Elmira, N. Y.
DAVIS, Calvin R. (jtf 1927), Br, Mgr. (for mail),
Johnson Service Co., 2328 Locust St., and 7534
Westmoreland Dr., St. Louis, Mo.
DAVIS, James R. (S 1034), 2111 Abington Rd.,
and (for mail), 9704 Miles Ave., Cleveland, Ohio.
DAVIS, Joseph (M 1927; A 1920), Owner, Htg.
Engr. and Contractor (for mail), 007 Root Bldg.,
70 W. Chippewa, and llJti Huntington Ave.,
Buffalo, N. Y.
DAVIS, Otis E. (M 1929; A 1925), 1501 Fourth
Ave., Scotts Bluff, Nebr.
DAVIS, Rowland G. (A 1921), Sales Repr., 887
Nela View Rd., Cleveland Heights, Ohio.
DAVISON, Robert L. (M 1934), Director of
Research (for mail), John B, Pierce Foundation,
40 West 40th St., and 2S East 10th St., New
York, N, Y.
DAWSON, Eugene F. (M 1034), Asst. Prof. Mcch.
Engr. (for mail), University of Oklahoma, and
910' S, mood St., Norman, Okla.
DAWSON, Thomas L. (M 1930), Pres, (for mail),
Thomas L, Dawson Co., 2035 Washington St.,
Kansas City, Mo., aud f)6th and Shawnee
Mission Rd., Rosedale Station, Kansas City,
Kans.
DAY, Harold C. (A 1934), Mgr., American
Radiator Co., 374 Delaware Ave., and (for mail),
Buffalo Athletic Club, Delaware Ave., Buffalo,
N. Y.
DAY, V. S.* (M 11)24) , En«n tfor mail), Carrier
Kngrg. Corp., 850 Krellnglmysen Ave., Newark,
and 100 Summit Ave., Summit. N, J.
DEAN, Charles L, (M 1032) f Asst, Prof, M«ch,
Engrg.. University of Wisconsin, and (for mail),
2603 Stevens St., Madison, Wia,
DEAN, Ffank J., Jr, 7s 19#4), Clerical, Automatic
Electric Co,, 1033 W, Van Buren, and (for mail),
12Q S, Central Ave., Chicago, 111.
DeBLOIS, Lewis A. (M 1034), Consulting Engr,,
485 East 57th St., New York, N, Y,
DEELY, James J, (J 1933), Sales Engr., Brooklyn
Union Gaa Co., 180 Remsen St., and (for mail),
Hotel St. George, Brooklyn, N, Y.
DeLAND, Charles W. CM 1024; J 1923), Secy-
Treas. (for mail), C. W. Johnson Co., Inc., 211
»N. Desplaines St., and 2021 Eatea Ave,, Chicago,
DENNY, Harold R, (A 1934), Mgr. Mereh, Dept,
American Blower Corp., 401 Broadway, New
York, N, Y.
DBUTCHMAN, Julius (/ 1935; S 1933), 1-3
Welleiley Ave,, Yonkera, N. Y.
DEWEY, &. P. (M 1984), Chief Engr, (for mail),
Barb«r~Colman Co., and 2301 Oxford St..
Rockford, 111.
DIBBLE, S. E** (M 1917), (Presidential Mamfow),
(Pres,, 1925: lat Vice-Pres*. 1924; 2nd Vice-
£re».» 1922; Council, 1921*1926). Supt., Thomas
Ran ken Patton School* BUssabethtown, Pa.
DICE, Eugene S. (5 1933), 7141 Upland St.,
Pittsburgh, Pa.
DICKENSON, Frederick R. (A 1934), Dist.
Mgr. (for mail), American Blower Corp., 1302
Swetland Bldg., Cleveland, and 3435 Menlo Rd.,
Shaker Heights, Ohio.
DICKEY, Arthur J. (M 1921), 9 Mossom Pi.,
Toronto, Ont., Canada.
DICKSON, Robert B, (M 1919), Pres. (for mail),
Kewanee Boiler Co., Inc., Franklin St. and Q
Tracks, and 409 E. Prospect St., Kewanee, 111.
D'IMOR, Elton J. (M 1933), Br. Mgr. and Engr.,
The Trane Co., LaCrosse, Wis., and (for mail),
ISO N. Auburndale St., Apt. 7, Memphis, Tenn.
DISNEY, Melvin A. (A 1934), Co-Partner,
Mfr's. Reprs., HtR., Vtg., and Air Cond. Equip,
(for mail), 4301 H Main St., and 8024 Merrier,
Kansas City, Mo.
DISTEL, Frank (M 1918), Owner, Distel Heating
Equipment Co., 404-406 Kalamazoo Plaza (for
mail), P. O. Box 133, and 1011 W. Genesce St.,
Lansing, Mich.
DIVER, M. L. (M 1925), Consulting Engr., P. O.
Box 1016, San Antonio. Texas.
DIXON, Arthur G. (A/ 1928), Sales M«r. (for
mail), Mocline Mfg. Co., and 442 Wolif St.,
Racine, Wis.
DOBBS, C. E. (A 1921), Rcpr., Burnham Boiler
Corp,, 31st and Jefferson Sta,t Philadelphia, Pa.,
and (for mail), 72 Berlin Ave., Haddonticld, N. J.
DODDS, Forrest F. (AJ 1920), Br. Mgr. (for mail),
American Radiator Co., 1023 Grand Ave., and
235 Ward Pkwy., Kansas City, Mo.
DODGE, Harry G. (A 1034), Vice-Pres., Metro-
politan Pipe & Supply Co., 14 fl Broadway,
Cambridge, and (for mail), 28 Rustic Rd.,
Melrose Highland, Mass.
DOERING, Frank L. (M 1010), Salesman,
American Radiator Co., 210 Denver Ave.r
DOHERTY, 'Russell (A 1920), Chicago Dist.
M«r. (for mail), National Radiator Corp,, 1111
East 8Hrd St., Chicago, and 300 Forest Ave.,
Oak Park, III.
DOLAN, Raymond G. {M 1920; A 1920; / 192ii),
Secy-Treas. (for mail), Tom Dolan Htg. Co.,
Inc., 614 W. Grand, and 2112 West 20th, Okla-
homa City, Okla.
DONNELLY, James A.* (M mm, (Treasurer,
1012-1914), Urgent, W. Va.
DONNELLY, RuaseH (M 1023), Sales Kngn (for
mall), Nash Engrg, Co., Graybar Bldg,, 420
Lexington Ave., New York, N. V.
DONOVAN, William J, (A 1930), 2239 North
27th St., Philadelphia, Pa,
DONZELLI, Enrico (U 1933), Piazza SS Pietro e
Lino, No. 4., Milan, Italy.
DORFAN, Morton I. (M 1020), Mgr, Du«t
Collecting l)iv,, Blaw-Knox Co,, f>, C), Box 1108,
and (for mail), 0357 Morrowfield Ave,, Pitts-
burgh, Pa.
DORNHEIM, G. A. (M 1912; J 1006), 15 Hamil-
ton Ave,, Brotixvilto, N, Y.
DORSE Y, Francis C. (M 1020), Engr, and
Contractor (for mall), Fnmdti C. Doraey, ine,,,
4520 Schenley Rd., Roland Park, and 212
Gittings Ave,, Baltimore, Md,
DOSTBR, Alexis (A 1634), sSecy. (for mail), The
Torringtori Mfg, Co., 70 Franklin S|,, Torrington*
and Lltchfield, Conn.
DOUGHTY, Charlos Jofett (M W»fi)t Prei, and
Managing Director (for mail), C. J» Doughty &
Co., F«d. Inc.. U, S. A»f 30 Brenan Rd,» aad 1020
Ave, Joffre, Shanghai* China,
DOVOLIS, Nick J. (S m&)> S403 Chicago Av«»,
Minneapolifl. Minn.
DOWNE, Edward R* (M 1927)* American Ga*
Products Corp., 40 Wett 40th St,» Nw York,
N. Y.
DOWNE, Henry S. (L$f* MMbtri M 1805) , Cl«
Natioaalc dcs Rtidiatoura, 140 Blvd. Hausaman,
ParifliFrance.
0OWNKS, Hftaty H* (M 1988) tMgr. Navy ftl^Lp*
Div. (for mall)» American Blower Coit>*» «*<
Woodward Bldg,, Wa«Wn8*0% D* C.» ana 460$
Davidson 0r.» Chevy Cfett«» ]Sld»
14
ROLL OF MEMBERSHIP
DOWNES, Nate W. (M 1917), (Council, 1928-
1930), Chief Engr. and Supt. of Bldgs. (for mail),
School Dist. of Kansas City, 317 Finance Bldg.,
and 2119 East 68th St., Kansas City, Mo.
DOWNS, Sewell H. (M 1931), Chief Engr.,
Clarage Fan Co., and (for mail), 211 Creston
Ave., Kalamazoo, Mich.
DOYLE, William J. (M 1920), Factory Mgr., The
Williamson Heater Co., 4558 Marburg Ave., and
(for mail), 3766 Hyde Park Ave., Cincinnati,
Ohio.
DRINKER, Philip* (M 1922), Assoc. Prof, (for
mail), Harvard School of Public Health, 55
Shattuck St., Boston, and Puddingstone Lane,
Newton Center, Mass.
DRISCOLL, William H.* (M 1904), (Presidential
Member), (Pres., 192G; 1st Vice-Pres., 192 A; 2nd
Vice-Pres., 1924; Treas., 1923; Council, 1918-
1927), (for mail), Thompson-Starrett Co., Inc.,
444 Madison Ave., New York, N. Y., and 50
Glen wood Ave., Jersey City, N. J.
DuBOIS, Louis J. (M 1931), Air Concl. Engr.,
York Ice Machinery Corp., 117 South llth St.,
and (for mail), 7337a Lindell Ave., St. Louis, Mo.
DUBRY, Ernest E. (M 1924), Asst. Supt., Central
Htg., The Detroit Edison Co., 2000 Second Ave.,
and (for mail), 9116 Dexter Blvd., Detroit, Mich.
DUDLEY, William Lyle (M 1922), Vice-Pres. (for
mail), Western Blower Co., 1800 Airport Way,
and S14-32nd Ave., Seattle, Wash.
DUFF, Kennedy (M 1915), Mgr. (for mail),
Johnson Service Co., 28 East 29th St., New
York, N, Y., and 9 Park Ave., Maplewood, N. J.
DUG AN, Thomas M. (M 1920), Sanitary and
Htg. Exifir., National Tube Co., Fourth Ave. and
Locust St., and (for mail), 1308 Freemont St.,
McKcesport. Pa.
DUGGER, Earl R. (S 1934), 8409 Classen,
Oklahoma City, Okla.
DUNCAN, George W-, Jr. (M 1923), 2512
Ben venue Ave., Berkeley, Calif.
DUNCAN, James R. (M 1923), Carrier Austra-
lasia, Ltd., 5(5 Hunter St., Sydney, Australia.
DUNCAN, William A. (A 1930), Dist. Service
Engr. (for mail), Dominion Oxygen Co., Ltd., 92
Adelaide St. W,, and 20 Tyrol! Ave., Toronto,
Out,, Canada.
DUNHAM, Clayton A.* (M 1911), Tres. (for
mail), C. A. Dunham Co., 450 1C. Ohio St.,
Chicago, arid lf>0 Maple Hill Rd., Glcncoc, 111.
DUKKEE, Merritt E, (A 1930), Sales Engr. (for
mail), C. A. Dunham Co., 101 Park Ave., New
York, and 254 Martina Ave,, White Plains, N. Y.
BURNING, Edward H. (J 1931), Commercial
Sales, Dallas Gas Co., Harwood and Jackson
Sta., and (for mail), 1880 Moaar St., Dallas,
Texas,
DURYEA, Albert A. (J 1935; S 1933), 151 Belden
Point, City Island, N. Y.
DUSOSSOIT, Edmond A. (M 1920), Treas, (for
mail), Lynch & Woodward, inc.. 320 Dover St.,
Boston, and 10 Hancock Ave,, Newton Center,
Mass,
DWYER, Thomas F. (M 1923), Meeh* Kngr. (for
mail), Board of Education, 49 Flatbueh Ave.
Ext., Brooklyn, and 1183 Clay Ave,, New York,
R Y,
DYER, Qrvilta 1C. (M 1919), Mgr.. Blower Div.
(for mail), Buffalo Forge Co,, 490 Broadway, sind
11 Rusted Ave.» Buffalo, N. Y.
E
EA0IE, John G, (M 1909), Eadie, Freund £
Campbell Co,, 110 West 40th St., New York,
N. VT
EAGAR, R, Frank (M. 1022), 98 Edward St.,
Halifax, N.S., Canada,
EAICINS, Walter (M 1928), 830 E, Phil Eltena
StM Germantown, Philadelphia, Fa,
EASTMAN, Carl B. (M 1932; A 1032; J 1929),
Mgr* Philadelphia Sake Ofta, C, A. Dunhajn
Co., 1500 walnut St., Philadelphia, and (for
mil), 7247 Calvin Ed,. Upper Darby, Pa, >
EASTWOOD, E. O. (M 1921), (Council, 1931-
1934), Prof, of Mech. Engrg. (for mail), Uni-
versity of Washington, and 4702-12th Ave. N.E.,
Seattle, Wash.
EATON, Byron K. (M 1920), 75 N. Park Rd.,
La Grange, III.
EATON, William G. M. (A 1934), Sales Engr.,
Pease Foundry Co., Ltd., US King St. E.,
Toronto 2, and (for mail), 59 Symington Ave.,
Toronto 9, Canada.
EBERT, William A. (M 1920), Mech. Contractor
(for mail), 1026 W. Ashby, and 2151 W. Kings
Highway, San Antonio, Texas.
EDWARDS, Daniel F. (M 1920), 2340-42 Pine
St., St. Louis, Mo.
EDWARDS, Don J. (.4 1933), Vice-Pies, (for
mail), General Heat & Appliance Co., 94 Massa-
chusetts Ave., Boston, and 40 Rockledge Rd.,
Newton, Mass.
EDWARDS, Paul A. (M 1919), Pres. (for mail),
The G. F. Higgins Co., 60S Wabash Bldg., and
3074 Pinehurst Ave., Pittsburgh, Pa.
EELLS, Henry B. (M 1926), New York Mgr.,
Barnes & Jones, Inc., 101 Park Ave., New York,
and (for mail), 1049 East 27th St., Brooklyn,
N. Y.
EGGLESTON, Lewis W. (M 1921), American
Radiator Co., 5961 Lincoln Ave., Detroit, Mich.
EGGLY, Harry J., Jr. (M 1933), Consulting
Engr. (for mail), 1805 Walnut St., Philadelphia,
and Elkins Park Apts., Elkins Park, Pa.
EHRLICH, M. William* (M 1916), Chief Engr.,
Commodore Heaters Corp., 11 West 42nd St.,
New York, N. Y., and (for mail), 56 Ridge Rd.,
Lyndhurat, N. J.
EICHBERG, W. Roy (M 1929), Pres. (for mail),
Carolina Sheet Metal Corp., 4210 Sansom St.,
Philadelphia, 'and 828 Turner Ave., Drexel Hill,
Pa.
EICHER, HuBert G. (M 1922), State Director,
School Bldgs., Div. Dept. of Public Instruction,
State Capitol, and (for mail), 103 South St.,
Harrisburg, Pa.
EISS, Robert M. (M 1933; ,4 1933; J 1930), (for
mail), 72 Brantwood Rd., c/o Buffalo N. Y. P. O.,
Eggertsville, N. Y,
ELLINGWOOD, Elliott L. (M 1909), 354 S.
Spring St., Los Angeles, Calif.
ELLIOT, Edwin (M 1929), (for mail), Edwin
Elliot & Co., 560 North 16th St., Philadelphia,
and 403 W. Price St., Germantown, Philadelphia,
Pa.
ELLIOTT, Louis (M 1932), Consulting Mech.
Engr., Electric Bond & Share Co., 2 Rector St.,
Room 1914, New York, N. Y. <
ELLIOTT, Norton B. &l 1934), Br. Mgr.,
American Blower Corp., 1011 Majestic Bldg.,
and (for mail), 5170 N. Idlewild Ave., Mil-
waukee, Wis.
ELLIS, Ernest E. (M 1922), Secy-Treas., F. A.
Ellis & Co., Inc., 840 Center St., Wirmetka, III.
ELLIS, Frederick E. (M 1923), Sales Mgr. (for
mail), Imperial Iron Corp., Ltd., 30 Jefferson
Ave,, Toronto, and 9 Princeton Rd., Kingaway
P, O. Toronto 3, Ontario, Canada.
ELLIS, Frederick R. (M 1913), Sales Engr.,
Buerkel & Co., Inc., 18*24 XJnion Park St.,
Boston, and (for mail), 131 Beacon St., Hyde
Park, Mass.
ELLIS, Harry W. (M 1923; A 1909), Pres.,
, Johnson Service Co., 507 E. Michigan St.,
Milwaukee, Wla,
EMERSON, Ralph R. (M 1922), 48 Gay St.,
Newtonville, Mass.
EMERY, Hugh (J 103tf; S 1933), 20 Morgan PL,
N. Arlington, N. J.
EMMERT.Lwther D. (M 1010), Repr. (for mail),
Buffalo Forge Co,, Room 1909, 20 N. Wacker
Dr.» Chicago, and 1704 Hinman Ave., Evanston,
111,
EMMONS, Neat L. (S 1984), 1100 East 19th,
Oklahoma City, Okla.
ENGEL, Edward (J 1933), Design Draftsman (for
mail), Hull Div., U. S. Navy Yard, and 2608
North 30th St,, Philadelphia, Pa.
15
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
ENGLE, Alfred (A 1923), Sales Mgr. (for mail),
Jenkins Bros., 80 White St., New York, and 1
Edgewood Rd., Scarsdale, N. Y.
EPPLE, Arnet B. (J 1934), Student Engr., B. F.
Sturtevant Co., Boston, and (for mail), 8 Elm St.,
Hyde Park, Mass.
EPPRIGHT, John O. (J 1934), 3928 Benton
Blvd., Kansas City, Mo.
ERDLE, Gardner F. (A 1933), Mfrs. Repr. (for
mail), 374 Delaware Ave., Buffalo, and 19
Trernont Ave., Kenmore, N. Y.
ERICKSON, Harry H. (.4 1929), Sales Engr.,
General Fittings Co., 804 Architects Bldg., and
(for mail), 5909 North 21st St., Philadelphia, Pa.
ERICKSON, Martin E. (A 1926), Supt., Main-
tenance, Board of Education, and (for mail),
1533 South 74th St., West Allis, Wis.
ERICSSON, Eric B. (M 1933), Engr., Custodian,
Board of Education, and (for mail), 605 West
116th St., Chicago, 111.
EVANS, C. A. (M 1919), 527 Massachusetts Ave.,
Buffalo, N. Y.
EVANS, Edwin C. (M 1919), Consulting Engr.,
2953 Zephyr Ave., Corliss Station P. O., Pitts-
burgh, Pa.
EVANS, William A. (M 1918), Mfr. and Agent,
W. A. Evans & Co., 180 Broadway, New York,
N. Y., and (for mail), 24 Woodland Rd., Maple-
wood, N. J.
EVELETH, Charles F.* (M 1911), 2030 East
115th St., Cleveland, Ohio.
EVERETTS, John, Jr.* (A 1935; J 1929), Engr.
(for mail), W. L. Fleisher, 11 West 42nd St.,
New York, and S3 Kenihvorth PL, Brooklyn,
N. Y.
EVLETH, Everett B. (A 1927), Div, Mgr. (for
mail), Minneapolis-Honeywell Regulator Co.,
43 E. Ohio, Chicago, and 1023 Ashland Ave.,
Wilmette, 111.
F
FABER, Dr. Oscar (M 193-1), Consulting Engr.
(for mail), Romney House, Marsham St., West-
minster, London and Hayes Court, Kenley,
Surrey, England,
FAGIN, Daniel J. (M 1032), Heating Engr.,
House Htg, Div., Laclede Gas Light Co.» llth
and Olive, and (for mail), 4920 Chippewa Ave.,
St, Louis, Mo.
FAHNESTOCK, Maurice K.* (M 1927), Re-
search Asst. Prof, (for mail), University of
Illinois, 214 M. E. Laboratory, and 701 W,
California St., Urbana, 111.
FAILE, Edward H* (M 1934), Consulting ICngr,,
E. H. Kaile Co., 44r Lexington Ave,, Hew York,
N. YM and (for mail), 1336 Fairfxeld Ave,,
Bridgeport, Conn.
FALTENBACHBR, Harry J, (,M 1930), 235 E.
Wister St., Philadelphia, Pa.
FALVEY, John 0. <M 1M)> 6686 Perahing Ave,»
University City, Mo.
FAMILETTI, A, Robert (J 1930)> 2812 Wtorton
St., Philadelphia, Pa.
FANSLER, P. E. (A 1927), Editor (for mall), Oil
Heat, 167 Madison Ave., New York, N, Y.. and
CatonsviUe, Md>
FARLEY. W. F, (M 1030), Saieaman, American
Radiator Co., 40 West 40th St., New York, and
(for mail), 28 Kirn St., New Rocheile, N. Y,
FARLEY, wuiouahby s. (j ioaa), partner,
Farley & Luther, 120 S. Union St., and (for mail),
Sill Montague St., Danville, Va,
FARNHAM, Roswell (M 1020), (Council, 1927-
1932), DIst. Mgr,, Knjprg, Sales ffor mail),
Buffalo Forge Co., P. O. Box 0S5, ana 5 Claren-
don PI., Buffalo, N, Y,
FARNSWORTH, John G. (J 1931), Gas House
Htg, Engr. (for mail), Central Illinois Light Co,,
310 S, Jefferson St., and 313 Crescent St., Peoria,
111.
FARRAR, Cecil W, (M 1020; A 1918), (Treai,,
1930; Council, 1980), Pres. (for mail), Excelso
Products Corp., ISO/ Klniwood Ave.» and 29
Oakland PL, Buffalo, N, Y,
FAUST, Frank H.* (J 1930), Engr., Air Cond.
Dept. (for mail), General Electric Co., 1 River
Rd., and 114 Union St., Schnectady, N. Y.
FAY, Francis G. (M 1925), Raisler Heating Co.,
129-31 Amsterdam Ave., New York, N. Y.
FEBREY, Ernest J. (M 1903), Htg, and Air
Cond. (for mail), 61G New York Ave, N.W., and
2331 Cathedral Ave., Washington, D. C.
FEEHAN, John B. (M 1923), Pres. and Treas. (for
mail), John B. Feehan, Inc., 471 Union St.,
Lynn, and 4 Ocean View Dr., Marblehead, Mass,
FEELY, Frank J. (.4 1929), 17215 Greenlawn,
Detroit, Mich,
FEGLEY, Donald R. (/ 1935; 5 1933), 2274
Loring PL, New York, N. Y.
FEHUG, John B. (M 1918), Pres. (for mail),
Excelsior Htg. Supply Co., 528 Delaware St., and
2927 Brooklyn Ave., Kansas City, Mo.
FELDMAN, A. M.* (Life Member; M 1903),
Consulting Engr., 40 West 77th St., New York,
N. Y
FELS, Arthur B. (M 1919), The Fels Co., 42
Union St., Portland, Maine.
FELTWELL, Robert H. (M 1005), Htg, Engr.,
U. S. Radiator Corp., 2321 Fourth St. N.E., and
(for mail), 1370 Oak St. N.W., Washington, D. C.
FENNER, N. Paul (A 192&), Hoffman Specialty
Co., 500 Fifth Ave., Room 3324, New York, N. Y.
FENSTERMAKER, Sidney E. (M 1909), Pres.
(for mail), S. E. Fenstermaker & Co., 937
Architects and Builders Bids;., and 3102 Washing-
ton Blvd., Indianapolis, Ind.
FERGUSON, Ralph R. (M 1934; A 1927; J 1925).
Mgr. Trade Dept., American Blower Corp., 401
Broadway, New York, N. Y., and (for mail),
100 Prospect St., Kast Orange, N. J.
FERNALD, Henry B., Jr. (J 193f>: S 1933), 145
Lorraine Ave., Upper Moutelair, N. J.
FERRERO, Henry J. (J 1935; 6' 1933), 1738
Adams St., New York, N. Y.
FIEDLER, karry William (M 1923), Pres. (for
mail), Air Conditioning Utilities, Inc., 480 Fifth
Ave., New York, and 49 Palmer Ave.» Scaradale,
N.Y,
FIFE, George I). (A 1931; J 1929), Kngr., Air
Cond., National Broadcasting Co., 30 Rocke-
feller Plaza, and (for mail), 102 Kast 2Snd St.,
New York, N. Y.
FILKINS, Harry L. (A 1933), Vice-Pres., City Ice
Co. of Kansas City, 21st and Campbell Sta., and
(for mail), 34 Kast 55 Terrace, Kansas City, Mo.
FltLO, Frank B. (A -1034), Minneapolis- Honey-
well Regulator Co., 2831 Olive St., St, Louis, Mo.
FIN AN, James Jf. (H 1923), Supervising Engr.,
Board of Education, City of Chicago, 228 N.
LaSalle St., Builders Bldg,, and (for mail),
7149 Euclid Ave., Chicago, III,
FINCH, Stanley k (A 1931), Industrial Engr.,
Brooklyn Union Caa Co., 180 Kemsen $t.»
Brooklyn, N. Y.
FIRESTONE, Jamoa F. (A 1025; J 1914), Exec.
Vice-Pros.* Round Oak Furnace Co,, and (for
mail), 203 Orchard St.» Dowagl&e* Mich,
FITTS, Ghnrlea JD. (M ItKZOl, Mgr. (for mail),
American Radiator Co., 692 Prior Ave.t St. Paul,
and 2807 Dean Blvd., Minneapolis, Mirm,-
HTTS, Joseph €. (M 1930), Secy.. Heating,
Piping ana Air Conditioning Contractor!
National Assn., 1260 Sixth Ave,» New York*
N. Y., and (for mail), 215 Kenilworth Rd,»
Mat
atthew J. (M 1034), Tre
Standard Asbestos Mfg. Con 820 W, Lake St»
and (for mail), 7314 Hanwd Ave,» CMctgQ, I1L
FITZSIMONS, J. Patrick C/ 19S4; S 1982), The
Robert FiUalmons Co,» Ltd., 21 Rebecca St*«
Hamilton, Ont.( Canada,
FLANAGAN, Edward T* (A 1929), C. A. Dunham
Co., Ltd., 1139 Bay St., Toronto, Ont.» Caimda.
FLARSHEIM, Clnr*mc« A. (J 1933), Mgr.> ^ir
Cond. DepU Stewart Warner-Atemite ' Co.,
2425 McGee St*» and (for mail), 8720 Holmes
St«» Kansas City, Mo.
FLBISHBH, Walter JU* <M 1014), Consulting
Engr. (for mall), 11 West 42nd &t,» New Yorfc,
and Saw Mill F&rm, New City, N. Y.
16
ROLL OF MEMBERSHIP
FLEMING, James P. (M 1923), Engr.- Custodian,
Board of Education, 5045 N. Kimball Ave.,
Chicago, 111.
FLINK, Carl H. (M 1923), Director of Research
(for mail), American Gas Products Corp., 408
East lllth St., New York, and 74 Brookside
Ave., Mt. Vernon, N. Y.
FLINT, Coll T. (M 1919), N.E. Sales Mgr. (for
mail), The H. B. Smith Co., 640 Main St.,
Cambridge, and 56 Brantwood Rd., Arlington,
Mass.
FLOYD, Morris (M 1933), Mgr., Air Cond. Div.,
Edwards Mfg. Co., Cincinnati, Ohio.
FOGARTY, Orville A. (M 1934), Mgr., Oil
Burner Div., Canadian Fairbanks-Morse Co.,
Ltd., 980 St. Antonie St., and (for mail), 2178
Old Orchard Ave., Montreal, Que., Canada.
FONDA, Bayard P. (M 1934), Air Cond. Engr.
(for mail), Bryant Heater Co., 17825 St. Clair
Ave., Cleveland, and 2905 Hampton Rd.,
Shaker Heights, Ohio.
FORFAR, Donald M. (M 1917), Mech. Engr. (for
mail), Grinnell Co., 240 Seventh Ave. S., and
4817 Emerson Ave. S., Minneapolis, Minn.
FORSBERG, William (M 1919), Hopson &
Chapin Mfg. Co., 231 State St., New London,
FORSYTH, Arthur T. (A 1934), Dist. Repr.,
Buffalo Forge Co., 2434 First Ave. S., Seattle,
Wash.
FOSTER, Charles (M 1923), Consulting Engr.
(for mail), 508 Sellwood Bldg., and 2831 E.
First St., Duluth, Minn.
FOSTER, James M. (M 1930; A 1920), Factory
Repr. (for mail), 4526 Olive St., St. Louis, and
7021 Lindell Ave., University City, Mo.
FOSTER, Tillman R. (J 1930), Carrier Engrg.
Corp., 180 N. Michigan Ave.> Chicago, 111,
FOUL0S, P. A. L. (M 1915), Mech. Engr. (for
mail), Office of Holhs French, Consulting Engr.,
210 South St., Boston, and 72 Whitin Ave.,
Point of Pines, Revere, Mass.
FOULDS, Samuel T. N. (J 1930), Sales Engr.,
Power Equipment Co., 791 Trcmont St., Boston,
and (for mail), 72 Whitin Ave., Revere, Mass.
FOWLES, Harry H. (J 1934), Heating Engr.,
Carman-Thompson Co., 12-14 Lincoln St.,
Lewiston, and (for mail), Y. M. C. A., Auburn,
Maine*.
FOX, Otto (M 1931), Chief Engr. (for mail),
Bryant Heater Co., 17825 St. Clair Ave., Cleve-
land, and 1819 Fannington Rd., East Cleveland,
Ohio.
FRAMPTON, Alfred C» (S 1984), 729>lJ Wilson,
Norman, Okla.
FRANK, John M. (M 1918: A 1912), Il« Elec.
Vtg, Co.. 2850 N. Crawford Ave., Chicago, 111.
FRANK, Olive B.* (Af 1010), Pwa. (for mail),
Frank Bngrg. Co., U Park PI., and 600 West
114th St., New York, N. Y.
FRANKEL, Gilbert S. (M 1920). Mgr., Federal
& Marine Dcpt. (for mail), Buffalo Forge Co.,
403 Commercial National Bank Bldg., and 2749
Macomb St. N.W., Washington, D, C,
FRANKLIN, Ralph S. (M 1019), Prea*Treas. (for
mail), Albert B. KrankUn, Inc,» 38 Chauncy St.,
Boston* and 320 Grove St., Melrose, Mass.
FREAS, Royal Bruce (M 1928), Pres. (for mall),
Freas Thermo Electric Co., 1206 S, Grove St.,
Irvington, N. J., and 4 West 43rd St., New York,
N. Y.
FREEMAN, Alton* M. (A 1©29)> Sales Engr.,
6088 Plankittgton Bidg», and (for mail), 4533 N.
Bftrtlett Ave., Milwaukee, Wla,
FREITAG, Frederic G, (M 1032), Consulting
Hngr, (for mail), Sylvestre Oil Co., 709 S.
Columbus Ave^ and 9 Harrison St., Mt. Vernon,
N. Y,
FRENCH, Donald (M 1926), Vice-Pres. (for
mail). Carrier Corp,, 850 Frelinffhuysen Ave.,
Newark, and 40 Waldron Ave,, Summit, N. J.
FRBY, Georftti O. (J 1984), Elec. Bnjpr. (for mail),
Warner Brou. Theatres, Inc., mi West 44th St.,
New York, and 221 Linden Blvd., Brooklyn,
N.Y,
FRIEDMAN, Ferdinand J. (M 1921), McDougall
& Friedman, 31 Union Square, New York, N. Y., ,
and (for mail), 1221 Osborne St., Montreal,
Que., Canada.
FRIEDMAN, Milton (S 1933), 470 West End
Ave., New York, N. Y.
FRITZ, Charles V. (S 1933), P. O. Box 303,
Carnegie Institute of Technology, Pittsburgh,
Pa.
FRITZBERG, L. Hilding (/ 1931), Engr. (for
mail), B. F. Sturtevant Co., and 1338 River St.,
Hyde Park, Boston, Mass.
FUKUI, Kunitaro (M 1920), Oriental Carrier
Engrg. Co., Ltd., Osaka Mitsui Bldg., Nakano-
shima, Osaka, Japan.
GABY, Frederick A. (M 1926), Chief Engr. (for
mail), Hydro-Electric Power Commission of
Ontario, 190 University Ave., and 480 Spadina
Rd., Toronto, Ont., Canada.
GALLIGAN, Andrew B. (M 1921), 716 South
51st St., Philadelphia, Pa.
GALLOWAY, James F. (S 1934), 176 Clarkson
Ave., Brooklyn, N. Y.
GAMMILL, Oscar E., Jr. (J 1930), Sales Engr.
(for mail), Carrier Engrg. Corp., 1416 Hibernia
Bank Bldg., and 2133 Calhoun St., New Orleans,
La.
GANT, H. P.* (M 1915), (Presidential Member},
(Pres., 1923; 1st Vice-Pres., 1922; 2nd Vice-
Pres., 1921; Council, 1918-1924), Vice-Pres. (for
mail), Carrier Engrg. Corp., 12 South 12th St.,
and Penn Athletic Club, Philadelphia, Pa.
GARDNER, S. Franklin (M 1911), Pres. (for
mail), Standard Engrg. Co., 2129 Eye St. N.W.,
and 4901 Hillbrook Lane, Washington, D. C.
GARDNER, William, Jr. (A 1921), Vice-Pres.
(for mail), Garden City Fan Co., 1842 McCor-
mick Bldg., and 7836 Loomis Blvd., Chicago, 111.
GARNEAU, L6o (J 1930), Sales Engr., Room 743
Dominion Square Bldg., and (for mail), 8454
Brouages St., Montreal, P. Q., Canada,
GAULT, George W. (S 1934), Marysville, Pa.
GAUSMAN, Carl E. (M 1923), Mech. Engr.,
1100 Minnesota Bldg., and (for mail), 2360
Chilcombe Ave., St. Paul, Minn.
GAUTESEN, AH (J 1935; 5 1933), 1039-79th St.,
Brooklyn, N. Y.
GAWTHROP, Fred H. (M 1919), Pres., Gawthrop
& Bro. Co., 705 Orange St., and (for mail), 2211
Shallcross Ave., Wilmington, Del.
GAY, Lewis M. (A 1934), Power Engr. (for mail),
Texas Power & Light Co., Box 902, Dallas, and
724 Griffith Ave., Terrell, Texas,
GAYLOR, William S. (M 1919), Consulting
Kngr,, Flameklng Co., Inc., 2159 Madison Ave,,
New York, and (for mail), 42 Mayhew Ave.,
Larchmont, N. Y.
GAYLORD, F. H. (M 1921), Western Sales Mgr.
(for mail), Hoffman Specialty Co., Inc., 130 N.
Wells St., Chicago, and 362 N. York St., Elm-
hurst, 111.
GEIGER, Irvin H. (M 1919), Reg. Prof. Engr. and
Mfrs. Repr,, Room 319 Telegraph Bldg., Har-
risburg, Pa,
GEISSBUHLER, John O, (S 1034), University
Circle, and (for mall), 9820 Zirnmer Ave.,
Cleveland, Ohio.
GELB, Amiel CS 1935), 1042 Irving Ave. N,,
Minneapolis, Minn,
GENCHI, Bernard (J 1935; 5 1938), 8808~15th
Ave., Brooklyn, N. Y.
GERMAIN, Oscar (M 1935), Germain Frere,
Ltd., 1343 Blvd. St. Louis, Three Rivers, Que.,
Canada.
GERRISH, Grenvllle B. (/ 1930), Mgr.. Fitz-
gibbona Boiler Co., Inc. ,,80 Boylston St., Boston,
and (for mail), 1 Overlook Rd., Melroee, Mass.
GERRISH, Harry E. (M 1610), (Coundl, 1919),
Vice-Frea, (for mail), Morgan-Gerrish Co., 807
Essex Bldg,, and 4584 Fremont St., Minneapolis,
Minn.
17-
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
GESMER, Joseph (J 1935; 5 1933), Student
Engr., B. F. Sturtevant Co., Hyde Park, and (for
mail), 41 Beacon St., Quincy, Mass.
GETSGHOW, George M. (Ad 1906), Pres. and
Treas. (for mail), Phillips Getschow Co., 32 W.
Austin Ave., and 4542 Beacon St., Chicago, 111.
GETSCHOW, Roy M. (M 1919), Secy, (for mail),
Phillips Getschow Co., 32 W. Austin Ave., and
1336 Arthur Ave., Chicago, 111.
GIANNINI, Albert A. (/ 1935; 5 1933), 64 West
170th St., New York, N. Y.
GIBBS, Edward W. (At 1919), (for mail), Smith-
Gibbs Co., 201 S. Alain St., and 234 President
Ave., Providence, R. I.
GIBBS, Frank C. (M 1921), Gen. Supt. (for mail),
National Regulator Co., 2301 ICnox Ave.,
Chicago, and 150 N. Cuyler Ave., Oak Park, 111.
GIESEGKE, Frederick E.* (M 1913), (Council,
1932-1934), Director, Texas Engrg. Experiment
Station, Agricultural and Mechanical College of
Texas, College Station, Texas.
GIFFORD, Clarence A. (A 1934), Salesman,
American Radiator Co., 374 Delaware Ave,, and
(for mail), 247 North Dr., Buffalo, N. Y.
GIFFORD, Robert L, (M 1908), Pres., Illinois
Engrg. Co., 21st St. and Racine Ave., Chicago,
III., and (for mail), 1231 S. El Molino Ave.,
Pasadena, Calif.
GIGUERE, George H. (M 1920), Mech. Engr.,
800 Marquette Bldg., and (for mail), 17205
Fairport Ave., Detroit, Mich.
GILES, Alfred F. (J 1934), H. H. Robertson Co.,
2000 Grant Bldg., and (for mail), 4307 Ludwick
St., Pittsburgh, Pa.
GILFRIN, George F. (M 1932), Gen. Repr. (for
mail), Carrier- Brunswick-International, Inc.,
Apartado 03, Bis and Paseo tie la Ret'orma 120,
Lomas de Chapultepec, Mexico, D, F.
GILL, John W. (S 1935), 2120 Carter Ave.,
St, Paul, Minn.
GILLE, Hadar B. (A/ 1930), Skoldungagatan 4,
Stockholm, Sweden.
GILLETT, M. C. (M 191(5), Engr., OUOO Rising
Sun Ave., Philadelphia, Pu.
G1LLHAM, Walter K. (/U 1917), (Trcas., 1920-
1929; Council, 19120-19129), Consulting Engr, (for
mail), 814 Inter-State Bids,, and 3427 Belief on-
taine Ave., Kansas City, Mo.
GILLING, William F., Jr. (Life Member; M 1933;
A 1919), Aast. Mgr., American Kadiator Co.,
127 Federal St., Boston, and (for mail), 2tt
Abbott Rd., Wellesley Hills, Mass.
GILMAN, Franklin W. (M 1935), Plant Engr,
(for mail), Atwater Kent Mfg. Co,, 4700 wfa-
aahickon Ave., and 5H W, Coulter St., Phila-
delphia, Pa,
GILMQRE, Louis A. (J 1935; 5 1930), Vice-Pres.
(for mail), John Gilmore & Co., 13 North 10th
St., and 01SG Westminster PI., St. Louis, Mo,
GILMOUR, Alan B. (A 1032), Salesman, B. K.
Gilmour Co., Inc., 15B-41at St., and (for mail),
410 Ocean Ave,, Brooklyn, N. Y.
GINJ, Aido (M 1933), via Correggio 18, Milano,
Italy.
GIVIN, Albert W. (,-1 ittiifl), The Guraey Foundry
Co,, Ltd,, P, O, Box 1149, Montreal, P. &„
Canada,
GLANZ, Edward (A 1930), Prea. (for mail),
Glanz & Killian Co,, 1701 W. Forrest Ave,> and
3865 Lake wood Ave., Detroit, Mich,
GLASS, William (A/ 1934), Mgr, (for mall).
Partridge- Halli day, Ltd., 144 Lombard St,,
Winnipeg, and 190 Braemar Ave,, Norwood,
Manitoba, Canada,
GLASSKY, J, Wilbur (M 1922), Partner (for
mail), Vapor Kngrg. Co,, 10 South 18th St,
Philadelphia, and 7818 Ardleigh St., Chestnut
Hill, Philadelphia, Pa.
GLEASON, Gilbert H, (M 1023), Partner (for
mail), Gilbert Howe Gieason & Co,, 2& Hunt-
ington Ave, Boston, and 10 Edgehlll Kd,»
Winchester, Mass,
GtOBJL Evlns Foree (A 1916). Pres., Evins F,
Glore Sales Corp., 1949 Grand Central Terrnin&U
and (for mail), 644 Riverside Dr., New York,
N. Y,
GOELZ, Arnold H. (M 1U31), Pres. (for mail),
ICrposchell Engrg. Co., 2300 N. Knox Ave.,
Chicago, and 8U7 Greenwood Ave., Wilmettc, 111.
GOENAGA, Ro&er C. (M 1031), Tech. Director
(for mail), Ateliers Ventil., 100 Cours Gambctta,
Lyon, and 33 Avenue Valioud, Ste Foy-les-lyon,
Rhone, France.
GQERG, B. (M 1928), (for mail), American
Radiator Co., 075 Bronx River Rd., Yonkers,
and 294 Bionxville Rd., Bronxville, N. Y.
GOLDBERG, Moses (.-1 1934), Pres., Electric
Motors Corp., 108 Centre St., New York, and
(for mail), 13 U E. Seventh St., Brooklyn, N. Y.
GOLDSGHM1DT, Otto E. (M 1«1.">), Consulting
Engr. (for mail), 110 West 10th St., and 345
Kast 57th St., New York, N. Y.
Ave., New York City Assn., 1045 Grand Central
Terminal Bldg., New York, N. Y., and (for mail),
1(50 Halsted St., Kast Orange N, ].
GOODRICH, Charles F. (A/ 1010), Andrews &
Goodrich, Inc., Boston, and (for mail), 330
Adams St., Dorchester, Mass.
GOODWIN, Samuel L. (4U 1024), Consulting
Engr,, 247 Madison Ave., Ilasbrouck Heights,
N. J.
3DV
Pittsburgh, and 0032 Marie St., Pittsburgh, Pa.
GORDON, Edward B., Jr. (M 1008), Pres.,
Pillsbury Engrg. Co., 1200 Second Ave,, and (for
mail), 2450 West 24th St., Minneapolis, Minn,
GORDON, Peter B. (J 1035), Kngr. (for mail),
George E. Gibson Co., 441 Lexington Ave,, New
York, N, Y., and 35 Park Ave., Bloomfidd, N. T.
GORDON, William J,, 4r, (6' 1035), 2208 Oliver
Ave, S., Minneapolis, Minn,
GORNSTON, Michael II. (A 1023), Stationary
Engr, (for mail), 430 Dumont Ave., Brooklyn,
and 8504 Woodhaven Blvd., Woodhaven, N. Y.
GOSSETT, Earl J. (M 1023), Pres, (for mail),
Bell & Goaaett Co., 3000 Wallace St., Chicago,
and 314 Woodland Ave., Winnetka, III,
GOTTWALD, C. (A 1910). Pres, (for mail), The
RiCMvIL Co., Union Trust Bldg,, Cleveland, and
2225 Stillman Rd., Cleveland Heights, Ohio.
GOULDING, William (A 1933), Kn«r«. Dent.,
National Broadcasting Co., Radio City. New
York, and (for mail), 409 Kast 17th St,, Brook-
lyn, N. Y.
GRAHAM, Charles H. (M 1034), Sales Engr,,
Lennox Furnace Co., Inc., Syracuse, and (lor
mail), 93 Lake St., Hamburg, N, Y,
GRAHAM, William D. (M 1920: A 1925; / 1923),
Dist. Mgr, (for mail), Carrier Engrg. Corp,, 8t>0
Union Trust Bldg,, Cleveland, Ohio,
GRAHN, Victor F, (M 1927), Htg. and Vtg,
Engr., fcnney & Ohmea, Inc., 101 Park Ave.,
New York, N, Y., and (for mail), 120 Greenwood
Ave,, East Orange, N, J.
GRA.NSTON, Ray O. (/ 1935; S 1030), Bn«r.>
Univ. Plbfr & Htg. Co,, 3039 University Way,
and (for mail), 4568 Fourth Ave, N,E,, Seattle,
Wash.
GRAJNT, Walter A. (A 1933; / 1929), Develop-
ment Engr., Carrier Eagrg. Corp,, 750 Fre-
Unghuysen Ave,, Newark, and (for mnil), H&Q
Anna St,, Elizabeth, N, J.
GRAVES, WUiurd B, (Life Mmfar; M 1000),
Pr«d, (for mail), W, B, Graves Htg, Co,, 102 N
,, Chicago, III
GRAY, E&rte W. (A 1834), Comm©rdai Otpt., la
Charge of Air Cond, Sales (for mail). Oklahoma
Gaa & Elec, Co,, Box 1408, aad 2125 N.W.,
18th, Oklahoma City, Qkla*
GRAY, Gyorfle A. (M l«M)f C, A, Duttham Co,,
Ltd,, 404 Flam BWg,» Ottawa, OntM Canada,
GRAY, Wlliiam E, (M IMS), Saiei
Powers Regulator Co., 2^720 Gr0^ftvl«w
j m., and (for mail), Bw 2
18
ROLL OF MEMBERSHIP
GREEN, Joseph J. (A 1938), Mfrs. Repr., Joseph
J. Green Co., Buffalo, and (for mail), 328 W.
Girard Blvd., Kenmore, N. Y.
GREEN, William C. (Life Member; M 1906),
Dist. Mgr. (for mail), Warren Webster & Co.,
704 Race St., and 244 Erkenbrecher Ave.
(Avondale), Cincinnati, Ohio.
GREENBURG, Dr. Leonard" (M 1932), Acting
Health Officer (for mail), New Haven Dept. of
Health, City Hall, 161 Church St., and 519
George St., New Haven, Conn.
GREENLAND, Sidney F. (M 1034), Htg. and
Vtg. Engr., Gee, Walker & Slater, Ltd., 32 St.
James St., London, S.W. 1, and (for mail), 71
Arodene Rd., Bnxton, London S.W. 2, England.
GREER, Willis R. (J 1934), Air Cond. Engr.,
Arkansas Power & Light Co., and (for mail),
' 1401 Linden St., Pine Bluff, Ark.
GRIFFIN, DeWitt C. (M 1933), Secy-Treas. (for
mail), May & Griffin, Inc., 501 Orpheum Bldg.,
and 9717~47th S.W., Seattle, Wash.
GRIFFIN, John ,T. (M 1921; A 11)18), Vice-Pres.
and Dir. (for mail), Mutual Bank and Trust Co.,
710 Locust St., and 3S52 Castlcman Ave., St.
Louis, Mo.
GROSECLOSE, John B. (A 1929), Engr.,
Estimator, Dixie Htg, & Vtg. Co., 109 Fannin
St., and (for mail), 3424 University Blvd.,
Houston, Texas.
GROSS, Lyman C. (M 1931), Consulting Engr.
4G53-13th Ave. S., Minneapolis, Minn.
GROSSMAN, Harry E. (.4 1033; J 1927), Sales
Repr., Haynea Selling Co., Inc., 1518 Fairmount
Ave., Philadelphia, and (for mail), 405 Custer
Ave., Glenoldcn, Pa,
GROSSMANN, Harry A. (M 1931), H, A.
Groaamann Co., 3221 Olive St., and (for mail),
3122 Gcyer Ave., St. Louis, Mo.
GUNTIIER, Felix A.* (M 1925), Sales Kngr. (for
mail), 429- B Oliver Bldg., and Box 220 R. D. 0,
S. Hills Branch, Pittsburgh, Pa.
GURNKY, Edward Holt (M 1020), (Council,
1031-15)34), Pres, (for mail), Gurney Foundry
Co., Ltd., 4 Junction Rd., and 347 Walmer Rd.,
Toronto, Ont, Canada.
H
HAAS, Emii, Jr. (J 1920), Secy-Treas. (for mail),
Natkin & Co,, 2020 Wyandotte, and Ncwbern
Hotel, Kansas City, Mo,
HAAS, Samuel L. (M 1023), Pros, (for mail),
- Advance Heating Co., 117-1U N. DespUuncs St.,
and 1T>13 Furtfo Ave., Chicago, 111.
HAATVEDT, Sheldon R. (,V 1035), ai5-10th
Ave. S.IC., Minneapolis, Minn.
HACKKTT, H. Berkeley at 1021), 901 Architects
BUlg.. 17th and Sansom Stsu, Philadelphia, Pa.
HADDOCK, Isaac IV (A 1026), New England Gas
& Elec. Assn., 710 Maaaachusetty Ave., Cam-
bridge, Masi.
HADEN, G. Nelacm (M 1034; A 1928; / 1922),
Director (for mail), G. N. Haden & vSona, Ltd.,
Lincoln House, 00 Kingeway, London W, C. 2,
and 36 Wild wood Rd., Hampsteart Heath,
London N.W, 1L England,
HADEN, William Nelson (Lift Mtmbv; M 1902),
Late Chairman, G. N, Haden & Sons, Ltd., St
Georges Works, and (for mail), Arnolds Hill,
Trowbrldge, Wilt, England,
HADESTY, Alfred L., Jr. (M 19*1), 130 E.
Broad St,t Tamnqua, Pa,
HADJISKY, Joseph N, <M 1980), Consulting
Engr., 744 Bates St., Birmingham, Mich,
HAGAN, WliUam V. (A 1933; J 3026), Secy, (for
mail), 608 Pearl St., and 1811 Jones St., Sioux
City, Iowa.
HAGfDON* Charles H* (M 1919), S, E, Fenatcf*
maker & Go,, W Architect! & Builder® Bldg.,
indiawtpoli*, tod.
HAIGNEV, Jfolm B, (J 193#t S 1988), 8621 Shore
Ed,, Brooklyn, N,,Y,
HAfNftSI* Jobia J* (M 1915). Free, (lor mail), Th«
HaineT Co,, 19*5 W, Late St., Chicago, and
S$0~J7th Av«,» Maywood, 111,
HAJEK, William J. (M 1932), Br. Mgr. (for mail),
Minneapolis-Honeywell Regulator Co., 285 Co-
lumbus Ave., and 333 Beacon St., Boston, Mass.
HAKES, Leon M. (M 1932; A 1932; J 1929), Sales
Engr. (for mail), The R. T. Coe Co., 400 Rey-
nolds Arcade Bldg., and 71 Stratmore Dr.-
Greece, Rochester, N. Y.
HALE, John F. (M 1902), (Presidential Member),
(Pres., 1913; 1st Vice-Pres., 1912; Board of
Governors, 1908-1910, 1912-1913), Dist. Mgr.
(for mail), Aerofin Corp., Ill W. Washington St.,
Rm. 1058, Chicago, and 408 S. Brainard Ave.,
LaGrange, 111.
HALEY, Harry S.* (M 1914), Consulting Engr.,
Partner (for mail), Leland & Haley, 58 Sutter St.,
and 735-21st Ave., San Francisco, Calif,
HALL, John R. (J 1032), Mech. Engr., U. S. Air
Cond, Corp., 2101 N.E. Kennedy St., and (for
mail), 141U Lakeview Ave., Minneapolis, Minn.
HALL, Mora S. (M 1934), Combustion Engr, (for
mail), May Oil Burner Corp., Maryland and
Oliver St., Baltimore, and Route No. 3, West-
minster, Md.
HAMBURGER, Fred G. (J 1935; 5 1933), 185
West 102nd St., New York, N. Y.
HAMENT, Louis (A 1933), Mgr. (for mail), Aqu-
atic Chemical & Metallurgical Engrs., 118 East
28th St., and 568 East 166th St., New York. N.Y.
HAMERSKI, Francis D. (J 1934), 626 E. Fifth
St., Winona, Minn.
HAMILTON, James E. (A 1933), Mgr. (for mail),
U. S. Radiator Corp., 4004 Duncan Ave., St.
Louis, and 7715 Shirley Dr., Clayton, Mo.
HAMUN, Chauncey J.T Jr. (.4 1934), Harnlin
Air Conditioning Co., and (for mail), 1014
Delaware Ave., Buffalo, N. Y.
HAMLIN, Harry A. (A 1910), Br. Mgr. (for mail),
Johnson Service Co., 427 Brainard St., Detroit,
and 120 Winona, Highland Park, Mich.
HANLEY, Edward V. (A 1933), Pres. (for mail),
S. V. Hanley Co., 1653 N. Farwell Ave., Milwau-
kee, and 844 E. Birch Ave., Whitefish Bay, Wis.
HANLEY, Thomas F., Jr, (M 1933), Pres. (for
mail), Hanley & Co., 1503 S. Michigan Ave., and
4940 East End Ave., Chicago, III.
HANSEN, Carl J. (J 1935; S 1933), 273 Sheffield
Rd., Lansclowne, Pa.
HANSEN, Charles C. (M 1928), Engr., 428
Prospect Sta., South Orange, N. J.
HANSON, Leslie P. (J 1935; S 1033), Engr., U. S.
Air Cond. Corp., and (for mail), 43«JB-46th Ave,
S., Minneapolis, Minn.
HARDING, Louis A,* (M 1911), (Presidential
Member'), (Pres., 1930; 1st Vice-Pres., 1929;
2nd Vice- Pres., 1928; Council, 1922-1931), Prea,
(for mail), L. A, Harding Construction Corp.,
Prudential Bldg., and 85 Cleveland Ave., Buffalo,
N. V.
HARE, W. Almon (M 1930), Pres., Hare Stoker
Corp.. 4853 Rivard St., Detroit, Mich.
HARMS, William T.* (M 1917), 1015 Vlnewood
Ave., Detroit, Mich.
HARRIGAN, Edward M. (M 1015), (for mail),
Harrigan & Keid Co,, 1366 Bagley Ave., and
7460 LaSalle Blvd., Detroit, Mich.
HARRINGTON, Charles (M 1923), 43 Indian
Grove, Toronto, Ont, Canada,
HARRINGTON, Elliott D.* (M 1932; A 1930),
Engr* (for mail). Air Cond. Dept., Commercial
Kngrff, DJv,, General Electric Co., 1 River Rd.,
and 1680 Wendell Ave», Schenectady, N. Y.
HARRIS, J«$a© B. (M 1018} , Pres. (for mail),
Rose & Harris Ena.» Inc., 416 Essex Bldg., and
3620 Colfax Ave. S., Minneapolis, Minn.
HART-BAKER, H«my W. (M 1018), Director
(for mail), Merritt, Ltd,, 8 French Bund, and
87 Rte Rene Delastre, Shanghai, China.
HART, Harrv M,* (M 1012), (PmidtntW
Jkfomto), (Fr<as,» 1916; 1st Vke-Pres,, 1915;
Council, 10144917), Pres. (for mail), L. H,
Prentice Co., 1048 Van Buren St., and 6409
( Wlntorop Ave., Chicago, 111.
HARTMAN, Fred Stewart (A 1938), Dist, Mgr.,
Industrial Dept- (for mail) , General Electric Co,,
170 Lexington Ave.» New York, N, Y,, and 168
Montckir Ave., Montdalr, N. J.
19
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
HARTMAN, John M. (M 1927), Engr. (for mail),
Kewanee Boiler Corp., and 719 Henry St.,
Kewanee, III.
HARTWEIN, Charles E. (M 1933), Supervisor,
House Htg. Dept., St. Louis County Gas Co.,
231 W. Lockwood, Webster Groves, and (for
mail), 6271 Magnolia Ave., St. Louis, Mo.
HARTWELL, Joseph C. (M 1922), (for mail),
Hartwell Co., Inc., 87 Weybosset St., and 10
Freeman Pkwy., Providence, R. I.
HARVEY, Alexander D. (A 1928; J 1925), Nash
Engrg. Co., South Norwalk, Conn.
HARVEY, Lyle C. (M 1928), Vice-Pres. (for mail),
Bryant Heater £ Mfg. Co., 17825 St. Clair Ave.,
and 3388 Glencarin RdM Cleveland, Ohio.
HASHAGEN, John B. (M 1930), 121 Manhattan
Ave., Jersey City, N. J.
HASLETT, Henry M. (5 1935), 950 Lombard
Ave., St. Paul, Minn.
HATEAU, William M. (J 1934), Draftsman and
Student, Sherron Metallic Corp., 1201 Flushing
Ave., Brooklyn, and (for mail), 1530 Sheridan
Ave., New York, N. Y.
HATTIS, Robert E. (M 1926), Consulting Engr.
(for mail), ISO N. Michigan Ave., and 4251 N.
Mozart St., Chicago, 111.
HAUAN, Merlin J. (M 1933), Consulting Engr.,
3412-16th S., Seattle, Wash,
HAUPT, Howard F. (A 1929), 614 E. Beaumont
Ave,, Milwaukee, Wis.
HAUSS, Charles F.* (Charter Member; Life.
Member), Via Gioberti No. 2, Milano, Italy.
HAYDEN, Carl F. (A 1930), Br. Mgr. (for mail),
Barber-Colman Co., 221 N. LaSalle St., Chicago,
and 2227 Ewing Ave., Evanston, 111.
HAYES, James J. (M 1920), Sales Engr. <for
mail), Stannard Power Equipment Co., 53 W,
Jackson Blvd., Room 925, and 7443 Jeffery Ave.,
Chicago, 111.
HAYES, John J. (A 1933), Auburn Stoker Sales
Corp., 40(J N. Wells St., Chicago, and (for mail),
918 Michigan Ave., Evanston, 111.
HAYES, Joseph G. (M 1908), Pres. and Engr.
(for mail), Hayea Bros.. Inc., 236 W. Vermont
St., and 2849 N. Capitol Ave., Indianapolis, Ind,
HAYMAN, A. Eugene, Jr., (J 1935; 5 1930),
2500 Washington St., Wilmington, Del.
HAYNES, Charles V, (M 1917), (Presidential
Member), (Pres., 1934; 1st Vice-Prea., 1933; 2nd
Vice-Pres,, 1032; Council, 102(5-1921), 11)32-1934),
Vice-Pres., Hoffman Specialty Co., 500 Fifth
Ave., Room 3324, New York, N. Y., and (for
mail), 115 Llanfair RcL, Ardmore, Mont. Co., Pa.
HAYTER, Bruce (M 1934), Chief Engr., Institute
of Thermal Research (for mail), American
Radiator Co., (575 Bronx River Rd., Yonkers,
and 49 Carman Rd., Scarsdalc, N. Y.
HAYWARD, Ralph B. (M 1009), Prea. (for mail),
R. B. Haywurcl Co., 1714 Sheffield Ave,, Chicago,
and 201 S. Stone Ave., LaGrange, III.
HEARD, John A. E. (J 1930), Carrier Engrg. Co.,
Ltd., Sardar Sujan Singh Block, Connaught PL,
New Delhi, India, and (for maiU, "Lyntan" 28
Leighcliff Rd,, Leighon-Sea, Eaaex, England.
HEARD, Roderick G. (A 1933), Asat. to Mgr,,
Fuel Oil Dept. (for mail), Imperial. Oil, Ltd.,
50 Church St., and 12 Huntley St., Toronto,
Ont., Canada.
HEATH, William R. (M 1031), Asat. Chief Engr.,
Buffalo Forge Co., 400 Broadway, and (for mall),
119 Wingate Ave,, Buffalo, N. Y.
HBBERUNG, G. W. (A 1934), Box 115, Wayzata,
Minn,
HBOHT, Frank H. (M 1930), Saks Engr. (for
mall), B» F* Sturtevant Co., 2635 Koppers Bidg.,
and 1467 Barnesdale St., Pittsburgh, Pa,
HECKEL. E. F. (M 1918), Vice-Pres. and Gen,
Mgr., Chicago Dist. (for mall). Carrier Engrg.
Corp.. 180 N. Michigan Ave., Chicago, and 314
Cuttriss PL, Park Ridge, 111.
HEDGES, H. Berkley (M 1019), 1021 Park Lane,
Plainfield, N. J,
HB0LBY, Park S. (M 1023), Park S. Hedley Co,,
Curtiss Bldg,, Delaware &t Tapper, Buffalo,
N, Y.
HEEBNER, Walter M. (M 1922^, Sales Engr.,
Warren Webster & Co., 470 Fourth Ave., New
York, N. Y., and (for mail), 282 Highwood Ave.,
Teaneck, N. J.
HEIBEL, Walter E, (M 1917), Dist. Mgr. (for
mail), Aerofin Corp., 11 West 42nd St., New
York, N. Y., and Old Greenwich, Conn.
HEILMAN, Russell H.* (M 1023), Senior
Industrial Fellow (for mail), Mellon Institute,
and 5G37 Wilkins Ave., Pittsburgh, Pa.
HELBURN, I. B. (M 1929; J 1927), Junior Assoc.
(for mail), Wyman Engrg., Chamber of Com-
merce Bldg., and 700 Clialfonte PL, Apt. 17,
Cincinnati, Ohio.
HELLSTROM, John (A 1929), Vicc-Prcs. (for
mail), American Air Filter Co., 215 Central
Ave., Louisville, and Anchorage, Ky,
HENDRIGKSON, Harold M. (M 1983), Mech.
and Refrigeration Engr., M. J. Hauan, Con-
sulting Engr., 324-1411 Fourth Ave., Bldg., and
(for mail), 7328 Earl Ave. N.W., Seattle, Wash.
HENDRICKSON, John J. (.-1 1932), Prod. Engr,
(for mail), Bryant Heater & Mfg. Co., 17825
St. Clair Ave., Cleveland, and 1475 Gcnessee
Rd., South Euclid, Ohio.
HENION, Hudson D. (A 1923), Sales Mgr. (for
mail), C. A. Dunham Co., Ltd., 1523 Davenport
Rd., and 45 Ridge Dr., Toronto, Ont., Canada.
HENRY, Alexander S.t Jr. (M 1930), 300 Central
Park West, New York, N. Y.
HERENDEEN, Frederick W. (At 1020), The
Institute of Boiler and Radiator Mfrs., 29
Seneca St., Geneva, N. Y.
HERKIMER, Herbert (M 1934), Director (for
mail), Herfcimcr Inst. of Refrigeration, 181J)
Broadway, and 25 Central Park West, New
York, N. Y.
HERLIHY, Jeremiah J. (Life Member; M 1914),
Pres. (for mail), J. J. Herlihy, Inc., 810 W»
Congress St., and 3(534 N. Keeler Ave., Chicago,
111.
HERRIOK, Daniel A, (M 1923), Gen. M«r, (for
mail), Julian d'Kete Co., 6 Spice St. (Charles-
town Dist.), Boston, and 27 Agassi/ St., Cam-
bridge, Mass.
HERRIOK, Leo (M 1935), Mgr, (for mail), Crane
Co,, and 323 Greenwood Ave,, Ft. Smith, Ark,
HERRING, Edgar CM 1010), Chairman and
Governing Director (for mail), J. Jeffreys & Co.,
Ltd,, Barrons PL, Waterloo Rd., London S.E.,
and "Kenia" Keswick Rd,, Putney, London
S.W., England.
HERRMANN, Harold C. (J 1935; S 1032).
Instructor, Milwaukee Vocational School, and
(for mail), 4523 North 22ncl St., Milwaukee, Wis,
HERTY, Frank B. (M 1933), House Htg, vSup-
erviaor, Brooklyn Union Ga@ Co., 180 Remaen
St., and (for mail), 50 Bast 18th St., Brooklyn,
N. Y.
HERTZLE&, John R,* (J W28), Air Cond. Saks
Engr. (for mail), York Ice Machinery Corp.,
42nd St. and Second Ave,, Brooklyn, and 1
University Pl,» New York, N, V,
HESS, David K. (J 1935; .$' HUM, Student (for
mail), 827 Mendota Court. Mttdtson, Wia,, and
Hess Warming & Vtg. Co,, mi-HJ27 S. Western
Ave,, Chicago, 111.
HESTER, Thomas J. (M 1010), Vice-Prew-Treas.
(for mall), Heater- Bradley Co., 283$ Washington
Blvd., and 67 Aberdeen PL, St. Louis, Mo,
HEXAMER, Harry D, (M 1931), ftilei Kngr. (for
mail), Kxcelso Products Corp.. rtft Clyde Ave.»
and 103 E. Delavan Ave., Buffalo, N, Y*
HEYDON, Charles G. (A 1923), Mgr. Sal«« of
Western Div., Wright-Austin Co., 315 W. Wood-
bridge St., and (for mail), 2681 Nebraska,
Detroit, Mich,
KftBBS, Frank G. (M 1017), Salesman, The H, B.
Smith Co., 2209 Chestnut St., and (for mail),
846 North 85th St., Philadelphia, Ft.
HICKEY, Daniel W. (A 1931), 278 W. Fourth St.,
St. Paul, Minn.
HICK.EY. J%m0a W. (J 1035; 3 1982), P. O. Box
245, Carnegie Institute of Technology* Pitts*
burgh* Pa,
20
ROLL OF MEMBERSHIP
HIERS, Charles R. (M 1929; A 1929; J 1927),
Mgr., Minneapolis-Honeywell Regulator Co.,
801 Second Ave., New York, and (for mail),
45-18-258th St., Great Neck, L, L, N. Y.
HIGGINS, Thomas J. (M 1927; A 1927; J 1923),
P. O. Box 17, East Dedham, Mass.
HILDEBRANDT, Henry A. (M 1918), Supt. of
Bldgs. and Grounds, University of Minnesota,
and (for mail), 708 Sixth Ave. S., Minneapolis,
Minn.
HILL, Dr. E. Vernon* (M 1914; A 1912), (Presi-
dential Member), (Pres., 1920; 1st Vice-Pres.,
1919; 2nd Vice-Pres., 1918; Council, 1915-1921),
Pres. (for mail), E. Vernon Hill Co., 121 N. Clark
St., and 1120 Farwell Ave., Chicago, 111.
HILL, Fred M. (M 1930), 225 East Ave. 39,
Los Angeles, Calif.
BILLIARD, Charles E. (M 1932; J 1927), Htg.
and Vtg. Engr. (for mail), E. C. Hilliard Co., 27
B St., South Boston, and 1301 Washington St.,
South Braintree, Mass.
HILLS, Arthur H. (M 1924), Mgr. (for mail),
Sarco Canada, Ltd., 725-G Federal Bldg., 83
Richmond St. W., Toronto, Ont., Canada.
HINCKLEY, Harlan B. (A 1934), Engr., Custo-
dian, Board of Education, S510 S. Green St., and
(for mail), 0933 Princeton Ave., Chicago, 111.
HINKLE, Edwin C. (Life Member; M 1911),
170 N. Franklin St., Hempstead, L. L, N. Y.
HINRICHSEN, A. F. (M 1928), Pres-Treas. (for
mail), A, F. Hinrichsen, Inc., 50 Church St.,
New York, N. Y., and Mountain Lakes, N. J.
HIRES, J. Edgar (M 1927), Pres. (for mail),
Hires, Castner & Harris, Inc., 200 South 24th
St., Philadelphia, and 107 Linwood Ave.,
Ardmore, Pa.
HIRSCHMAN, William F. (M 1929), Pres. and
Chief Engr., W. F. Hirschman Co., Inc., 220
Delaware Ave,, Buffalo, and (for mail), 105
Le Brun Circle, Eggertsville, N, Y,
HITCHCOCK, Paul C. (M 1931), Partner (for
mail), Burlingame & Hitchcock, Consulting
Engrs., 520 Sexton Blelg., and 4939 Girard Ave.
S., Minneapolis, Minn.
HJBRPE, Clarence A,, Jr. (J 1931), 73 Arch St.,
New Britain, Conn.
HOBBS, J, Clarenqe (M 1920), 60 Wood St.,
Painesvillc, Ohio.
HOCHULJU Henry W. (M 1925), Sales Engr,,
National Radiator Corp., 55 West 42nd St., New
York, N. Y., and (for mail), 113 Chester Ave.,
Bloomlield, N. J.
HODEAUX, W, L. (M 1931), Owner (for mail),
W, L. Hodeaux Plbg. & Htg, Co., 216-17 N,
fclagler Dr., and 310-lOth St., West Palm Beach,
Fla.
H0DGDQN, Harry A. (Ad 1919), 153 Norfolk St.,
Wollaaltm, Mass.
HODGE, William B, (M 1034), VIcc-Prea., Parka
Cramer Co., and (for mail), F, O. Box 1234,
Charlotte, N. C.
HOFFMAN, Charles S, (M 1924), Vice-Pres. (for
mail), Baker Smith & Co., Inc., 570 Greenwich
St. and 75 Central Park W., New York, N, Y.
HOFFMAN, James D,* (M 1903), (Presidential
Umber), (Pres., 1D10: 1st Vice-Pres., 11)08;
Board of Governors, 1911-11)12), Prof, of Practi-
cal Mechanics, Head of Dept., Director of
Practical Mech. Lab. (for mall), Purdue Uni-
versity, and 828 University St., W. Lafayette,
Ind,
HOFT, Paul J. (M 1025; A 1924), (for mail), 245
8. Eighth St., and 1119 Wyoming Ave,, Phila-
delphia, Piw
HOOAN, Edward L,* (M 1911), Consulting Engr,
(for mall), American Blower Co,, 6000 Rusaell
St., and 700 Sewatd Ave,, Detroit, Mich,
HOLBEOOK, Frank MJ* (M 1023), Enfir,, 62
Walnut Crescent Montclair, N. J.
HOIXA0AY, William L. (A 1988), Mgr., Engrg,
Dept, (for mailj, The George Belaey Co,, Ltd.,
1001 S. Hope St., LOB Angeles, and 110 Loma
Alt*. Dr,. Altadena, Calif,
HQLUSTER, B, Wallace (J 1931), Owner,
HoUUter'i* 21 Bay St., Glens Falls, and (for
mall), 88 Oak St., Hudson Falls, N. Y,
HOLLISTER, Norman A. (M 1933), Repr., The
Trane Co., 122 East 42nd St., New York, and
(for mail), 7101 Colonial Rd., Brooklyn, N. Y. '
HOLMES, Richard E. (J 1934), Engr., Air Cond.,
Westinghouse Elec. & Mfg. Co., E. Springfield,
and (for mail), 11 Bushwick St., Springfield,
Mass,
HOLT, James (M 1933), Asst. Prof, (for mail),
Massachusetts Institute of Technology, Cam-
bridge, and 1062 Massachusetts Ave., Lexington,
Mass.
HOLTON, John H. (M 1927), Asst. Chief Engr.
(for mail), Carrier Engrg. Corp., 850 Freling-
huysen Ave., Newark, and 5 Mountain Ave.,
Maplewood, N. J.
HOOD, O. P. (Honorary Member 1929), (for mail),
Chief, Technologic Br., U. S. Bureau of Mines,
17th and F St. N.W., and 1831 Irving St. N.W.,
Washington, D. C.
HOOPER, Vernon F. (M 1929), Gl Eastern Ave.,
Ossining, N. Y.
HOPPER, Garnet H. (M 1923), Engr., Taylor
Forbes, Ltd., 1088 King St. W., and (for mail),
19 Brummel Ave,, Toronto, Ont., Canada.
HOPSON, William T. (Life Member; M 1915),
The Hopson & Chapin Mfg. Co., New London,
Conn.
HORNUNG, John, C. (M 1914), Engr. (for mail),
Central Heat Appliances, 343 S. Dearborn St.,
Chicago., and 854 Bluff St., Glencoe, HI.
HORTON, Homer F. (M 1925), Sales Repr. (for
mail), National Regulator Co., 2301 Knox Ave.,
Chicago, 111.
HOSHALL, Robert H. (M 1930), Associate (for
mail), Thos. H. Allen, Consulting Engr., 65
McCall St., and 789 N. Evergreen St., Memphis,
Tenn.
HQSKING, Homer L. (M 1930), Br, Sales Mgr,
(for mail), Pacific Steel Boiler Corp., 370 Lexing-
ton Ave., New York, and 5 Church Lane,
Scarsdale, N, Y.
HOSTERMAN, Charles O. (M 1924), Supt., The
McMurrer Co., 303 Congress St., Boston, and
(for mail), 25 Bateswell Rd., Dorchester, Mass.
HOTCHKISS* Charles H. B. (M 1927), Heating
and Ventilating, US Lafayette St., New York,
N, Y.
HOUGHTEN, Ferry C.* (M 1921), Director (for
mail), Research Lab., A.S.H.V.E. Bureau of
Mines, 4800 Forbes St., and 1136 Murray Hill
Ave., Pittsburgh, Pa.
HOULISTON, G. Baillie (A 1928), Secy, (for
mail), W. C. Green Co., 704 Race St., Cincinnati,
Ohio, and 112 Forest Ave., Ft. Thomas, Ky.
HOWARD, Ed&ar (S 1936), 2721 Blaisdell Ave.,
Minneapolis, Minn.
HOWATT, John* (M 1915), (1st Vice-Pres.,
1934: 2nd Vice-Pres., 1933; Council, 1927-1934),
Chiet Engr, (for mail), Board of Education, 228
N. LaSalle St., and 4940 East End Ave., Chicago,
III
HGWELL, Frank B. (M 1920), Tech. Advisor
(for mail), American Radiator Co., 40 West 40th
St, and 15 Central Park W., New York, N. Y.
HQWELL, Lloyd (M 1915), Htg., Vtg. and Air
Cond. Engr,, Peoples Gaa Bldg., 122 S. Michigan
Ave., and (for mall), 7601 Yates Ave., Chicago,
III,
HOWLETT* Ira G. (S 1934), 2132 N, PonshUl
Ave,, Oklahoma City, Okla,
HOYT, Charles W, (A 1931), Pres-Treae. (for
mail), Wolverine Htg. and Vtg, Equip, Co., 80
Boylston St, Boston, and 45 Thaxter Rd,,
Newtonville, Maas*
HOYT, Leroy W, (M 1930), N. Stamford Ave,,
Stamford, Conn.
HUBBARD, George Wallace* (M 1011), Chief
Mech, Engr. (for mail), Graham, Anderson,
Probst & White, 1417 Railway Exchange,
Chicago, and 710 Bonnie Brae, River Forest, 111.
HUGH, A, J. (M 1919), Secy-Treas, (for mail) ,
Central Supply Co., 312 S. Third St, and 4087
Harriet Ave., Minneapolis, Minn. '
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
HUCKER, Joseph H. (M 1921), Partner, Hucker-
Pryibil Co,, 1700 Walnut St., Philadelphia, and
(for mail), 715 Stanbridge St., Norristown, Pa.
HUDSON, Robert A. (M 1934), Consulting Engr.
(for mail), Hunter & Hudson, 41 Slitter St.,
R. 710, and 2850 Union St., San Francisco,
Calif.
HUETTNER, Henry F. (S 1934), 124 Jerusalem
Ave., Hicksville, L. L, N. Y., and (for mail),
Box 388, Carnegie Tech., Pittsburgh, Pa.
HUFFAKER, Herbert B. (ill 1933), 209 N. Tenth
St., Council Bluffs, Iowa.
HUGHES, Charles E. (S 1934), 140 Beacon Ave.,
New Haven, Conn.
HULL, Harry B. (M 1931), Mgr., Research
Engr., Frigidaire Corp., and (for mail), P. O.
Box 671, Dayton, Ohio.
HUMPHREY, Dwight E.* (M 1921), Htg. and
Vtg. Engr., Goodyear Tire & Rubber Co., 1144
E. Market St., Akron, and (for mail), 2499 Sixth
St., Cuyahoga Falls, Ohio.
HUMPHREYS, Clark M. (M 1931), Asst. Prof, of
Mech. Engr. (for mail), Carnegie Institute of
Technology, Schenley Park, and 1934 Remington
Dr., Pittsburgh, Pa.
HUNGER, Robert F. (M 1927), Associate Dist.
Mgr. (for mail), Buffalo Forge Co., 703 Cunard
Bldg., and 4618 Chester Ave., Philadelphia, Pa,
HUNGERFORD, Leo (M 1930), Pres. (for mail),
Pacific Elec. & Mech. Co., Inc., 524 Loew's State
Bldg., and 105 N. Berendo St., Los Angeles,
Calif.
HUNT, Noel P. (M 1934), Managing Dir. (for
mail), Carrier Australasia, Ltd., 50 Hunter St.,
and 52 Lang Rd., Centennial Park., Sydney,
N.S.W.. Australia.
HUNZIKER, Chester E. (A 1934), Br. Mgr. (for
mail), American Blower Corp,, 331 State St.,
Schenectady, and 422 Reynolds St., Scotia, N. Y.
HUSKY, S. T. (S 1934), 710 Monnett St., Nor-
man, Okla.
HUST, Carl E. (At 1932), Htg. Engr. (for mail),
The Union Gas & Elec. Co., Room 1008, Fourth
and Main Sts., and Hillcrest Apts., 15 Mason St.,
Cincinnati, Ohio.
HUSTOEL, Arnold M. (A 1030), 12023 N. Ballou
St., Chicago, III.
HUTGHINS, William II, (M 1934), Chief Engr,,
Delco Appliance Div., General Motors Corp,,
and (for mail), 88 Magee St., Rochester, N. Y.
HUTZEL, Hugo F. (M 1918), Mgr., Erskine
Radiator Div. (for mail), Chase Brass & Copper
Co,, Inc., and 72 Hewlett St., Waterbury, Conn.
HVOSLEF, Fredrik W. {M 19U1; A 1921), Htg.
Research Kngr, (for mail), Kohler Co,, and 52tt
Autlubon Rd., Kohler, Wia.
HYDE, Lawrence L, (J 1934), Gen. Mgr,, M. J.
O'Ncil, and (for mail), M S. Cretin St., St. Paul*
Minn.
HYMAN, Wallace M. (M 1920), Pres. (for mail),
Rots & O'Donovan* Inc., 12 West 21st St., and
23 West 73rcl St., New York, N. V,
HYNES, Lee F,* (M 1010), (for mail), 240 Cherry
St., Philadelphia, ?a,, and Haddoafield, N, J.
I
ICKERINGILL, J. a (AT 1923), Engr.. Spencer
Heater Co., 2504, N. Broad St., and (for mail),
23S Rector St., Philadelphia, Pa.
ING ALLS, Frederick D. B. (M 1906), Consulting
Engr,, 1 Hopkins St., Reading, Mass.
INGELS, Margaret* (M 1928; J 1018), Mech.
Engr, (for mail), Carrier Engrg. Corp., 8&0
Freunghuysen Ave., Newark*, and Hotel East
Orange, Bast Orange, N. J.
INGOLD, John W. (7 1035; S 1938), 3038 Perry-
ville Ave. N.S., Pittsburgh, Pa.
INNIS, Helm R* (M 1921; J 1918), Urgent,
W.Va.
I8SERTELL, H«nry G,* (M m3; A 1912),
Consulting Engr., 81 Park Terrace W., N<sw
York, N. Y,
JACKSON, Alton B. (M 1932), 15 Hcrrick St.,
Winchester, Mass.
JACKSON, Charles H. (M 1923), Vice-Pres. (for
mail), Blower Application Co., 918 N. Fourth St.,
and 2700 N. Farwell Ave., Milwaukee, Wis.
JACKSON, Marshall S. (M 19110, Rcpr. (for
mail), Powers Regulator Co., 250 Delaware Ave.,
and 10S Larchniont Rd., Buffalo, N. Y.
JACOBUS, Dr. David S (Lifc Member; Al 1910),
The Babcock & Wilcox Co., 85 Liberty St.,
New York, N. Y.
JALONACK, Irvviii G. (A 1933; 6' 1930), Knsrg.
Mgr. (for mail), c/o A, L. Hart, 82 Railroad Ave.,
and 15 South St., Patchotfue, N. Y.
JAMES, Hamilton R. (A/ 1931), Service Kquip.
Engr., United Engineers & Constructors, Inc.,
1401 Arch St., Philadelphia, and (for mail), 55
W. Drexcl Ave., Lansdowne, Pa.
JAMES, John W * (7 1933), 2223 Grand Blvd.,
Schenectady, N. Y.
JANET, Harry L. (Al 19130), KHRI. (for mail),
Carrier Engrg. Corp., Chrysler BUltf., New York,
and 688 DecaturSt., Brooklyn, N. Y.
JARDINE, Douftlas C. (M 102'); A 102t>), Pres.
(for mail), Jardine & Knight Plbg. & Ht«. Co.,
312 N. Custer Ave., and 1512 K, Platte Ave.,
Colorado Springs, Colo.
JARRATT, Paul R. (.4 1031), 117 Fifth Ave. N.,
Nashville, Temi,
JELLETT, Stewart A.* (Uonvmry .Uembfr 1920),
(Charter Member; Presidential Alcmber), (Pres.,
1805; Board of MRW.» 1800-1800; Secy., 1808),'
42(> W. Kllet St., Germantown, Philadelphia, Pa.
JENNEY, Hu&h B. (.1 1033), Sales M«r., Domi-
nion Radiator & Boiler Co., Ltd., Royce and
Lansdowne Avcs., Toronto, Ont., Canada,
JENNINGS, Irving 0. (At 1024), Prow, (for mail).
Nash Engrg. Co., and 138 Flax Hill Rd,, South
Norwulk, Conn.
JENNINGS, Warren G. (A 1030), Minueapolia-
Honeyvvell Regulator Co,, 43 E. Ohio St.,
Chicago, 111.
JENN1NS, Henry H. (Life Member; M 1001),
lf> Grange View, Chapeltown Rd.» Leeds,
JENJ5?ON(f Joan S. (M 1012), Consulting Engr. (for
mail), Neiler-kkh & Co., 431 S. Dearborn St.,
and 1634 West 100th St., Chicago, 111.
JKPERT1NGER, Richard C. (A 1034), Gen,
Mgr. and Engr. (for mail), hyncromtitic Air
Cond, Corp., 1317 N. Third St., and 1028 W.
Vienna St., Milwaukee, Wia.
JOHN, Victor P. (M 1031), 13(5 Herryman Dr.,
Snydcr, N, Y.
JOHNS, Harold B.* (M 1028} J 1027), (for mail),
Peoples Gas Co., 122 S. Michigan Av<a., Chicago,
and 543 N. Klmwood Ave,, Oak Park, 111.
JOHNSON, Carl W. (Af 11)12). Pres. (for mall),
C. W. Johnson Co., Inc., 211 N, Desplainoi St.,
and 1800 Morse Ave.» Chicago. III.
JOHNSON* Clarence W. (M 19^3; A 1938;
J mi), Br, Mgr, (for mail), Canadian Sirocco
Co., Ltd., 030 Dorchester Si, W,, and 3^3
Dresden Ave., Mt. Royal, Montreal, P, Q,,
Canada,
JOHNSON, Edward B, (M 1019). Sates Engr,,
Staten lalaml Supply Co,, and (for mail), lf>4
Wardwell Ave,, W, New Brighton, N. Y.
JOHNSON, Edftar Jtt, (M 1020), Sales Engr. (for
mail), Buffalo Forge Co., 490 Broadway, and 103
University Ave., Buffalo, N. Y.
JOHNSON, H«te* S. (A 1083; J 1027), Buffalo
Forge Co,, 414 Standard Bldg., Albany, N. Y,
JOHNSON, Leslie 0. (J" 1930), c/o Y.M.CA,,
White Plains, N, Y.
JOHNSON, Louis H. (M 1031), 918 USftlte Av«,,
Minneapolis, Minn,
JOHNSTON, HU&O 0» (A 1984), Coatraotor»
Jleating & Ssmitary Service, Box W2» Wttllington
0»L, Canada.
JOHNSTON, J* AmWter (M 101»), Ftrtner tf<sr
mull), Carneal Johnston & Wrtilit, 80S
Bidg*. Richmona, Va*
ROLL OF MEMBERSHIP
JOHNSTON, Robert Elliott (M. 1929; A 1926),
3342-33rd Ave. W., Vancouver, B. C., Canada.
JOHNSTON, William H. (M 1924), 306 East
26th St., New York, N. Y.
JONES, Alfred (M 1928), Chief Consulting Engr.
(for mail), Armstrong Cork Co., P. O. Box 540,
402 President Ave., Lancaster, Pa.
JONES, Alfred L. (M 1926), Plbg. and Htg.
Contractors (for mail), 21 Church St., Green-
wich, and Box 121, Riverside, Conn.
JONES, Bernard G. '(M 1928), Mgr. (for mail),
Acme Fan & Blower Co., Ltd., 868 Arlington St.,
and 542 Raglan Rd., Winnipeg, Man., Canada.
JONES, Charles R. (A 1928), Jones Supply Co.,
Siloam Springs, Ark.
JONES, Edwin (M 1933; J 1924), Box 582, Tulsa,
Okla.
JONES, Edwin A. (M 1919), Chief Engr. (for
mail), L. J. Mueller Furnace Co., 2001 W.
Oklahoma, and 4065 N. Prospect, Milwaukee,
Wis.
JONES, Edwin F. (M 1923), Consulting Engr.,
420 New York Bldg., and (for mail), 220 Mont-
rose PL, St. Paul, Minn.
JONES, Harold L. (M 1920), Asst. Supt. (for
mail), W. W. Farrier Co., 44 Montgomery St.,
Jersey City, and 11 Cambridge Rd., Glen Ridge,
JONES, Noel W. (/ 1935; 5 1933), 1315 East 28th
St., Minneapolis, Minn.
JONES, Raymond E. (M 1919), Asst. Supervisor,
Fuel Oil Sales, Gulf Refining Co., 1515 Locust
St., Philadelphia, Pa., and (for mail), 39 West
End Ave., Haddonfield, N. J.
JONES, William T. (M 1915), (Presidential
Member'), (Pres,, 1933; 1st Vice-Pres., 1932; 2nd
Vice-Pres., 1931; Council, 1925-1934), Treas.,
Barnes & Jones, 128 Brookside Ave., Jamaica
Plain, and (for mail), 1886 Beacon St., Waban,
Mass.
JORDAN, Lebcrt E. (A 1934), Engr. (for mail),
Minneapolis Air Conditioner Co., 1609 Hennepin
Ave., and 122 Arthur Ave,, S.K., Minneapolis,
Minn.
JORDAN. Richard C. (/ 1935; S 1933), Air Cond.
Engr., Central Supply Co,, 312 S. Third St., and
(for mail), 2518 Grand Ave. S., Minneapolis,
JOYCE, Harry B. (M 1922), Consulting Engr. (for
mail), 810 Commerce Bldg., and 501 Liberty St,
Erie, Pa.
JUNG, John S. (M 1930; A 1923), Heating
Contractor (for mail), 2409 W. Greenfield Ave,,
and 1510 S. Layton Blvd,, Milwaukee, Wis.
JtJTTNER, Otto J. (M 1915), Pres, (for mail),
Tuttner Htg. Co., 814 N. Milwaukee St., and 910
E. Wells St., Milwaukee, Wis.
KAGEY, I. B., Jr-* (/ 1929), Air Cond, Engr.,
Metropolitan Life Insurance Co,, 1 Madison
Ave.r New York, N. Y.
XCAHAN, Charles (J 1935; S 1038), 6 Marie Ave,,
Cambridge, Mass,
JCAHNSKY, Alex G, (S 1934), 137QG Durkec
Ave,, Cleveland, Ohio,
KAMMAN, Arnold R* (A 192A; J 1921), (for
mall), Park S. Hedky Co., 304 Curtiss Btdg,,
Buffalo, and Wanakah, Eric Co., N, Y,
KAMPISH, Nick B, (S 1984), 214 E, Lincoln
* Ave., Roselle Park, N, J, - ^ ^ -
KAJPPEL, George W, A. (M 1921), Pres. and
Treas. (for mall), Camden Heating Co., Wilson
Blvd. and Waldorf Ave,, Camden, and 347 W.
Kings Highway, Haddonfield, N, J.
St Louis (J 1035; S 1983), 00$ E. Pearl
* Of 1918), Chief Engr. (for
mail), Parks-Cramer Co., 970 Main St, Fitch-
burg, and 180 Prospect St., North teominster,
Mass*
KARTORIB, V. T. (/ 19S5j 3 1988), Graduate
A«it, fa Meeh, Engr,, Case School of Applied
Seteacft, and (for mall), 2982 $ut 102nd St.,
Cleveland, Ohio.
KASTNER, George G. (J 1935; 5 1033), Sales
Engr., Schwerm Air Cond. Corp., 2303 Grand
Concourse, and (for mail), 654 East 226th St.,
New York, N. Y.
KAUFMAN, William M. (J 1935; S 1933), 2875
Sedgwick Ave., New York, N. Y.
KEEFE, Edmund T. (M 1931), 75 Pitts St,,
Boston, Mass.
KEENEY, Frank P. (A 1915), Pres., Keeney
Publishing Co., 6 N. Michigan Ave., Chicago, 111.
KEHM, Horace Stevens (M 1928), Pres. (for
mail), Kehm Bros. Co., 51 E. Grand Ave., and
5510 Sheridan Rd., Chicago, 111.
KELBLE, Frank R. (M 1928), Vice-Pres. and
Mgr. (for mail), Huff man- Wolfe Co. of Phila-
delphia, 11 W. Rittenhouse St., Philadelphia, and
115 Roslyn Ave., Glenside, Pa.
KELL, Waldo R. (A 193i), Sales Engr. (for mail),
The Marley Co., 1915 Walnut St., and 113 East
69th Terrace, Kansas City, Mo.
KELLEY, James J. (A 1024), Vice-Pres. and Gen.
Mgr. (for mail), Arthur H. Ballard, Inc., 535
Commonwealth Axre., Boston, and 142 Gover-
nors Ave., Medford, Mass.
KELLNER, Day C. (S 1933), (for mail), Carnegie
Institute of Technology, Pittsburgh, Pa., and
Cuba City, Wis.
KELLOGG, Alfred (M 1916), (Council, 1920-
1921, 1923-1924), Consulting Engr. (for mail),
585 Boylston St., Boston, and C Hawthorne St.,
Belmont, Mass.
KELLY, Charles J. (M 1931), New York Repr.,
Jas. P. Marsh Corp., 551 Fifth Ave., New York,
and (for mail), 162 Fairview Ave., Jersey City,
N. J.
KELLY, Hugh (M 1927), Mgr. (for mail), H,
Kelly & Co., Ltd., 10041-101 A Ave., and
10235-124th St., Edmonton, Alberta, Canada.
KELLY, John G. (A 1919), 374 Park Ave.,
Yonkers, N. Y.
KENDALL, Edwin H. (A 1932; J 1930), 309
West 12th St., Los Angeles, Calif.
KENNEDY, Maron (J 1930), Sales Engr. (for
mail), York Ice Machinery Corp., 5051 Santa Fe
Ave., and 2037 Bronson Ave., Los Angeles, Calif.
KENNEDY, Owen A. (3 1933), Carnegie Institute
of Technology, Pittsburgh, Pa.
KENNEDY, Paul V. (S 1934), 105 Avon St.,
New Haven, Conn., and (for mail), 4915 Forbes
St., Pittsburgh, Pa.
KENT, J. King (J 1928), Pres. (for mail), J. King
Kent & Co., Inc., 0327 Clayton Ave., and 5041
Waterman, St. Louis, Mo.
KENT, Laurence F, (A 1927; J 1924), Pres. (for
mail), Moncrief Furnace Co., P. O. Box 1673,
Atlanta, and R. F. D. No. 2, Smyrna, Ga.
KENWARD, Stanley B. (J 1935; 5 1933), 45
Fifth Ave,, Bay Shore, N. Y.
KEPLER, Donald A* (S 1934), Gibba & Cox, Inc.,
11 Broadway, New York, N. Y., and (for mail),
30 Maplewood Ave., Maplewood, N. J.
KEPLINGER, William L. (M 1929), Special
Repr. (for mail), Carrier Kngrg. Corp., 408
Chrysler Bldg., New York, and 103 Sunset Dr,f
Hempatead, L. I., N. Y.
KEPPNER, Harry W* (U 1930), (for mail),
H, W. Keppner, 1310 South 56th Ave., and 1245
S. Austin Blvd., Cicero, 111.
KERN, Raymond T- (M 1927), Chief Engr,,
Jenmaon Co., Pitchburg, and (for mail), 51
Claflin St., Leorainster, Mass.
KERSHAW, Melville O. (M 1932; A 1926;
J 1921), Vtg, and Air Cond, Engr. (for mail),
E, I, Du Pont de Nemours & Co., Wilmington*
Del, and 7313 North 21st St., Philadelphia, Pa.
KEYES, Robert E. (M 1918), Chief Engr., The
Cooling & Air Conditioning Corp., 24 Damon St.,
Hyde Park, Boston, Mass,
KEYS, Lee Farls (S 1934), Asat. Air Cond. Engr.,
Metropolitan Life Insurance Co., 1 Madison
Ave., New York, N. Y., and (for mail), Route 1,
Booc 866, Phoenix, Ariz.
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
KIGZALES, Maurice D. (M 1935), Assoc. Mech.
Engr., U. S. Army Motion Picture Service,
State, War and Navy Bldg., and (for mail).
3000 Connecticut Ave. N.W., Washington, D. C.
KIEFER, Carl J. (M 1922), Consulting Engr. (for
mail), 918 Schmidt Bldg., and 984 Lennox PL,
Cincinnati, Ohio.
KIEFER, E. J., Jr. (A 1932; J 1928), Treas. and
Gen. Mgr. (for mail), H. C. Archibald Co., 8 S.
Sixth St., and 10S N. Sixth St., Stroudsburg, Pa.
KIESLING, Justin A. (M 1930), Pres. (for mail),
Robischimg-Kiesling, Inc., 4S4S Main St., P. O.
Box 1295, and 1806 Holman Ave., Houston,
Texas.
KILNER, John S. (M 1929), Owner (for mail),
Kilner Co., 427 Stormfeltz-Loveley Bldg., and
1091 Seminole Ave., Detroit, Mich.
KIMBALL, Charles W. (M 1915), Richard D.
Kimball Co., 6 Beacon St., Boston, Mass.
KIMBALL, Dwight D.* (M 190S), (Presidential
Member), (Pres., 1915; 2nd Vice-Pres., 1014;
Board of Governors, 1912-1910), Consulting
Engr. (for mail), 205 East 42nd St., and 307 East
44th St., New York, N. Y.
KING, Roy L. (J 1935;, 5 1933), 2538 Clinton
Ave. S., Minneapolis, Minn.
KIPE, J. Morgan (M 1919), 801 Homestead Ave.,
Beechwood, Del. Co., Pa.
KIRK, Charles D. (M 1909), Mgr. (for mail)*
Chas. D, Kirk Co., Sargent & Colleen, and 774
McMillan Ave., Winnipeg, Man., Canada.
KIRKPATRICK, Arthur H. (7 1931), Ilg
Electric Vtg. Co., 415 Brainard St., and (for
mail), Webster Hall Hotel, Detroit, Mich.
KIT AURA, Shigeyuki (M 1918), 191 Shimo-
ohsaki, near Tokyo, Japan.
KITCHELL, Herbert N. (A 1926), 4528 Circle
Ave., Cincinnati, Ohio.
KITCHEN, Francis A. (A 1927; J 1923), Pres.
(for mail), American Wanning & Ventilating Co.,
1514 Prospect Ave,, and 1711 Ivenyon Rd.,
Cleveland, Ohio.
KITCHEN, John H, (M 1906), Owner (for mail),
John H, Kitchen Co., 1016 Baltimore Ave., and
5015 Westwood Terrace, Kansas City, Mo.
KLEIN, Albert (M 1920), Managing Director (for
mail), Carrier Lufttechnische Gcscllschaft m b H,
Stuttgart, Archivstrasse 14/16, and Stuttgart,
Panoramastrasse 23, Germany.
KLEIN, Edward W. (M 1917), S. E. Diet. Mgr,
(for mail), Warren Webster & Co., 152 Nassau
St. N.W., and 456 Peachtree Battle Ave.,
Atlanta, Ga.
KLIE, Walter (M 1915), Prea. (for mail), The
Smith & Oby Co,, 0107 Carnegie Ave., Cleveland,
and 18411 S, Woodland Ave., Shaker Heights,
Ohio,
KNIBB, Alfred E. (M 1930), Htg. Engr, (for mail),
1003 Maryland Ave., and 9333 E. Jefferson Ave,,
Detroit, Mich,
KNOPF, Charles (J 1935; S 1933), 1201 Liberty
Ave., Brooklyn, N, Y.
KNOX, James R. (U 1930), Htg, Engr., c/o
Carmichael, 93 Arbroath Rd,, Dundee, Scotland,
KNUDTSON, Carl M. (S 1935), 2410 Cromwell
Dr., Minneapolis, Minn,
KOCH, Harry O. (M 1916), 212 Centre St.,
Tamaq.ua, Pa.
KOHLER, Walter J-T Jr. (A 1983), Htg. Sales
Supervisor (for mall), KohW Co., and 005 W.
Park Lane, Kohler, Wia.
KOLINSKY, Max D, (S 1035), 418 Concord St.,
St. Paul, Minn.
KONZO, Selchi* (/ 1032), Special Research
Associate, Engrg. Experiment Station. University
of Illinois, 214 Mech. Engr. Lab., and (For mall),
1108 W, Stoughton St., Urbana, 111.
KO01STRA, John F. (M 1033), Engr. (for mail).
Carrier Bngrg. Corp,, 748 E. Washington, and
6063 Roy St., Los Angeles, Calif.
KORN, Charles B. (M 1922), Member of Firm,
Reber«Korn Co., 817 Cumberland St., and (for
.mail), 1022 S. Eighth St., Allentown, Pa.
KOTTCAMP, Horace A. (M 1915), Gen. Mgr.
(for mail), Kottcamp Construction Co., 147 N.
Second St., and 527 Philadelphia Ave., Chambers-
burg, Pa.
KOZU, Tamiichro (U 1930), No. 1701 Yonchome,
Shimoochai, Yodobashiku, Tokyo, Japan.
KRAMIG, Robert E., Jr. (A 1933), Vice-Pres.
and Treas. (for mail), R. E. Kramig & Co., 222
East 14th St., Cincinnati, and 51 Central
Terrace, Wyoming, Ohio.
KRATZ, Alonzo P.* (M 1925), Research Prof.
(for mail), Dept. of Mech. Engrg., University of
Illinois, and 1003 Douglas Ave., Urbana, 111.
KREISSL, Hans George (M 1925), Mgr. "Vento"
Dept. (for mail), American Radiator Co., 816
S. Michigan Ave., Chicago, and 408 Lee St.,
Evanston, 111.
KRIEBEL, Arthur E, (M 1920), Sales En&r. (for
mail), Haynes Selling Co., 1518 Fairmount Ave.,
Philadelphia, and Berwyn, Chester Co., Pa.
KRUEGER, James I. (M 1921), Mfrs. Repr. (for
mail), 357 Ninth St., and 1920 Sacramento St.,
San Francisco, Calif.
KRUSE, Robert W. (A 1930), Krusc Co., 353
West IGth PL, Indianapolis, Ind.
KUEHN, Walter C. (A 1933), Kuelm Htg. & Vtg.
Co., 915 Seventh Ave. S., Minneapolis, Minn.
KUEMPEL, Leotx L. (/ 1929), 3836 Vincent Ave.
S., Minneapolis, Minn.
KUHLMANN, Rudolf (A/ 1928), 122 East 42nd
St., New York, N. Y.
KUNS, Joseph W. (S 1935), 2110 Hawthorne
Ave., Minneapolis, Minn.
K.WAN, I. K. (/U 1933), Gen. Mgr., China Engrg.
Co., 30 Brenan Rd., Shanghai, China.
KYLBERG, V. C. (A 1934), tK)7 Ridgewoud Rd.,
Maplewood, N. J.
LAGODZINSKI, H. J. (A 1927; J 1920), 8028
N. Tripp Ave,, Chicago, III.
LAN0AUER, Leo L, (J 1932), Mech. Kn«r. (for
mail), Kribs & Lamlauer, Consulting Kngrs.,
807 S. W. Life iiklg., and 5707 Voluaco St.,
Dallas. Texas.
LANDERS, John J. (M 11)30; A 1924: J 1024),
Sales Engr, (for mail), Pacific Steel Boiler Corp.,
303 Crosby Bldg., Buffalo, and Seneca St.,
Kbcnezcr, N. Y.
LANE, 0. Dufly (M 1934), Supervisor, The
Servicing Corp. of New York, 101-10 Jamaica
Ave., Jamaica, and (for mail), 30*33-3Gth St.,
Jackson Heights, N, Y.
LANGE, Fred F. (A 1934), Engr. (for mail),
Mechanical Service Co.» 04 1 Northwestern Bank
Bldg., and 626a-28th Ave. S3., Minneapolis, Minn.
LANGBNBERG, E, B, (M 1014), (Council, 1926-
1981), Prea. (for mail), Langenberg Heating Co.,
3800 W. Pine Blvd., and 6031 Snrijiht, St. Louis,
Mo.
LANNING, E, K. (A 1927), Warren Webster &
Co,, Camden, N. J.
LANOU, J, Ernest (M 1931), Mgr. (for mail),
F. S, Lanou & Son, 90 St. Paul St., and 48 Brookea
Ave., Burlington, Vt.
LARSON, GiMtu* L.* (M 1028), (2nd Vice-Pros,,
1934; Council, 1929-1034), Prof,, Steam and Gas
Engrg., and Chairman of Dept* of Mech, Engrg.,
University of Wisconsin. MadJaon, Wis.
LftSALVlA» James J, (M 1930), Air Cond. Engr.,
Frigidaire Corp. and (for mail), Commodore
Apts., 522 Grand Ave,, Dayton, Ohio,
LAUTENSCHLAGER, Ft«d (M 1915), Viefc-
Pre8*Treaa. (Offices Kroeschell Boiler Co,,) 8253
Kedsie Ave., Chicago (factories), 100 Eelchert
Ct., Racine, Wis», and (for mail)» 3840 Atta
Vista Terrace, Chicago, III
LAW3LER. Mutthew M, <J 1980), Eeeident Mgr.
(for mail), Kitchen Engrg, Co», Inc** 1U w.
Washington St., and 6900 N, Aahtamd Blvd.,
Chicago, III.
LAWTON, Frank a (M 102S), 145 Euena ViiU
Ave., Hawthorne, N. J.
ROLL OF MEMBERSHIP
LEDNUM, J. Maynard (M 1934), Engr., Silica
Gel Corp., Baltimore Trust Bldg., and (for mail),
4203 Linkwood Rd., Baltimore, Md.
LEEK, Walter (M 1903), Managing Director (for
mail), Leek & Co., Ltd., Htg. Engrs., 1111
Homer St., and 4769 W. Second Ave., Vancouver,
B. C., Canada.
LEES, Herbert K. (M 1924; J 1912), (for mail),
548 Washington Blvd., and 5855 N. Kenneth
Ave., Chicago, 111.
LEES, John T. (J 1935; 5 1933), 1218 N. New St.,
Bethlehem, Pa.F and (for mail), 60 Boylston St.,
Cambridge, Mass.
LEFFINGWELL, Robert R. (J 1935; S 1933),
2747 Sedgwick Ave., New York, N. Y.
LEGLER, Frederick W. (A 1933), Mgr., Retail
Sales (for mail), Waterman- Waterbury Co., 1121
Jackson St. N.E., and 2919 Johnson St. N.E.,
Minneapolis, Minn.
LEIGH, Robert L. (J 1935; 5 1933), 1034 Cadillac
Dr., Grand Rapids, Mich.
LEILICH, Roger L. (M 1922), Pres. (for mail),
Baltimore Heat Corp., 2000 W. Pratt St., and
2810 Elsinor Ave., Baltimore, Md.
LEINROTH, J. Paul (M 1929), Gen. Industrial
Fuel Repr. (for mail), Public Service Electric &
Gas Co., SO Park PL, Newark, and 37 The
Fairway, Montclair, N. J,
LEITCH, Arthur S. (M 1908), Pres. and Manag-
ing Director (for mail), The Aithur S. Leitch Co.,
Ltd., 1123 Bay St., and 421 Russell Hill Rd.,
Toronto, Ont, Canada.
LELAND, Warren B. (M 1929), Sales Engr., The
H. B. Smith Co., Westfield, and 34 Leyfred
Terrace, and (for mail), P. O. Box 1522, Spring-
tield, Mass.
LELAND, William E. (M 1915), Partner (for
mail), Leland & Haley, 58 Sutler St., San
Francisco, and 704 The Alamecla, Berkeley,
Calif,
LBNNON, Joseph O. (M 1929), Mgr. (for mail),
llg Electric Vtg. Co., 15 Park Row, and 180
West f>l)th St., New York, N. Y,
LEONARD, J, 1L (M 1931), Mgr. (for mail), J. H,
Leonard Co., 508 Scott Bldg., and 844 Grosvenor
Ave., Winnipeg, Man., Canada.
LEOPOLD, Charles S. (M 1934), 213 S. Broad
St., Philadelphia, Pa.
LESLIE, Donald E. (J 1935; 6' ,1933), 3541
Bloomington Ave., Minneapolis, Minn.
LEUPOLD, Herbert W. (J 1933), Engr., Metro-
politan Life Insurance Co., 1 Madison. Ave., New
York, and (for mail), 35-15-MOth St., Flushing,
N, Y.
LEVY* Marion L (J 1931), Salea Mgr. arid C.
Kngr. (for mail), Air Controls, Inc., Div. of
Cleveland Heater CQ,, ItWO West 114th St., and
1273 West 108th St., Cleveland, Ohio.
LEWIS, Carroll E, (M 1930), Pres, (for mail),
Lewis Air Conditioners, Inc., 829 Second Ave. S.,
Minneapolis, and 145-1 CUelmaford St., St. Paul,
Minn.
LEWIS, Georfte C, (M 1919), Vice-Prea. and
Treaa. (for mail), American Htg. & Vtg, Co,,
1505 Race St., Philadelphia, and 812 Summit
Grove Ave,, Bryn Mawr, Pa.
LEWIS* Jolm G» (M 1026), 412 East 31st St.,
Kansas City, Mo.
LEWIS, L. Loftaa* (M 1918), Secy, (for mail),
Carrier Bngrg. Corp*. 850 FreUnghuysen Ave.,
Newark, and 724 Carlton Ave,, Plainfkld, N. J,
LEWIS, Sarnmsl R,* (M 1906), (Pruidmttot
Mmfor)t (Pm.» 1914; 2nd Vlce-Pres., 1910;
Board of Governors! 1909-1910-1912; Council,
1914*1915), Consulting Engr, (for mail), 407
S, Dearborn St., and 4737 JGnabark Ave.,
Chicago, m,
LEWIS, Thornton* (M 1910), (Presidential
}, (Pres,, 1929; 1st Vice-Press., 1928; 2nd
sn 1927; Council, 1923-1030), Executive
a, (for mail), Carrier Bngrg, Corp., $50
Frellnghuynen Ave,, Newark, ana 4 Halsey PL,
South Orange, N. J.
LIBBY, Ralph S. (7 1933), Canadian Sumner
Iron Works, Ltd. (Stoker Division), 560 Vernon
Dr., and (for mail), 575 East 50th Ave., Van-
couver, B. C., Canada.
LICHTY, Charles P. (M 1920), Pres. (for mail).
C. P. Lichty Engrg. Co., Inc., 400^ South 21st
St., and 125 Windsor Dr., Birmingham, Ala.
LINDBERG, Arthur F. (J 1935; 5 1933), Supt.,
U. S. Dept. of Interior, and (for mail), 14S4 Van
Buren St., St. Paul, Minn.
LINN, Homer R. (M 1914), Engr., Western Exec.
Office, American Radiator Co., 816 S. Michigan
Ave., Chicago, and (for mail), 321 S. Ashland
Ave., La Grange, 111.
LINTON, John P. (M 1927), Managing Director
(for mail), The Garth Co., 50 Craig St. W., and
247 Brock Ave. N., Montreal, West, Canada.
LIVINGSTON, Bernard B. (M 1927), Gas Engr.
(for mail), Dept. of Public Utilities, Box 976, and
1630 Monument Ave., Richmond, Va.
LLOYD, Edward C. (M 1927), (for mail), Arm-
strong Cork & Insulation Co., and 429 W.
Walnut St., Lancaster, Pa.
LOCKHART, Harold A. (J 1935), Engr. (for
mail), Bell £ Gossett Co., 3000 Wallace St., and
7906 S. Carpenter St., Chicago, 111.
LOEFFLER, Frank X. (M 1914), Pres. (for mail),
Frank Loeffler Supply Co., 710 N. Hudson St.,
and 320 West 26th St., Oklahoma City, Okla.
LOEFFLER, Louis, Jr. (S 1934), 1815 W. Ninth
St., Oklahoma City, Okla.
LOFTE, John Allen (J 1935; S 1933), (for mail),
Carnegie Institute of Technology, Pittsburgh,
Pa., and Mondovi, Wis.
LOH, Nan-Shee (M 1933; A 1931; J 1927),
House 42, Lane 88, Connaught Rd., Shanghai,
China.
LONG, David Raymond (M 1927), Pres.,
Tageraft Corp., 142 S. Christian St., and (for
mail), 150 School Lane,. Lancaster, Pa.
LONGCOY, Grant B. (M 1933), Maintainance
Engr., Cleveland Board of Education, and (for
mail), 1462 Wyandotte Ave., Lakewood, Ohio.
LOO, Ping Yok (<M 1933), Gen. Mgr. (for mail),
China Engrg. Co., No. 35-36 Chung Ling Feng
Hsin Chia Kow, Chung San Rd., Nanking, and
271-273 Dumbarton Rd., Tientsin, China.
LOVE, Clarence H. (M 1919), Mfrs. Agent,, Nash
Engrg. Co., 317 Chamber of Commerce, and (for
mail), 289 Norwalk Ave., Buffalo, N. Y.
LOWE, Howard H. (J 1935; S 1932), 1800 Fourth
St. S.E,, Minneapolis, Minn.
LOWNSBERY, Benjamin F. (M 1920), Htg.
Engr., Benjamin F. Shaw Co., P. O. Box 953, and
(for mail), 21 S. Sycamore, St., Wilmington, Del.
LOWY, M. R. (J 1935; 3 1933), 2305 Loring PL,
New York, N. Y.
LUCK, Alexander W.* (Life Member; M 1919),
Pres. and Gen. Mgr. (for mail), Reading Heater
& Supply Co., Church and Woodward Sts.,
Reading and Reiffton, Pa.
LUCKE. Charles E. (M 1924), Consulting Engr,,
Babcock & Wilcox Co., 85 Liberty St., and
Stevens Prof, of Mech. Engrg. (for mail),
Columbia University, Physics Bldg., and 110
Riverside Dr,, New York, N. Y.
LUNJD, Clarence E. (S 1933), Lab. Asst., Uni-
versity of Minnesota, Experimental Engrg.
Bldg., and (for mail), 2729-lSth Ave. S., Minn-
eapolis, Minn.
LUPIENT, Gerald C. (S 1935), 212 Bedford St.,
Minneapolis, Minn.
LUTY, Dpnald J. (M 1933) » Asst. Mgr., Air
Cond. Div. (for mail), Gar- Wood Industries,
Inc., 7924 Riopelle St., Detroit, and 911 Forest
Ave., Ann Arbor, Mich.
LUTZ, James H., Jr. (M 1928), Owner (for mail),
140 Paxton St., and loOl Forster St., Harrisburg,
Pa,
LXJTZ, Walter J. (7 1935; 5 1933), c/o S, A. E.
House, 4915 Forbes St., Pittsburgh, Pa.
X. (M 1919), Vice-Pres., Carrier
XJjjG*, J&irnQaL J. « v*1** *v*'t'JL YJ,<-C-A *«*»., VH»A**I*J.
Engrg. Corp., Room 408, Chrylser Bldg,, New
York, N. Y;
25
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
LYLE, J. Irvine* (M 1911), (Presidential Member] ,
(Pres., 1917; Council, 1917-1918), Pres. (for
mail), Carrier Corp., 850 Frelinghuysen Ave.,
Newark, and 1200 W. Seventh St., Plainfield,
N, J.
LYMAN, Samuel E. (.4 1924), 850 Frelmghuyscn
Ave., Newark, and (for mail), 728 Canton St.,
Elizabeth, N. J.
LYNCH, William L. (M 1928), Treas. & Genl.
Mgr., (for mail), Rome Turney Radiator Co.,
and 1413 N. George St., Rome, N. Y.
LYNN, John H. (A 1933), charge Air Cond.
Dept., (for mail), Texas Automatic Sprinkler
Co., and 3431 Shenandoah St., Dallas, Texas.
LYON, P. S. (M 1929), Commercial Kngrg Div.,
Air Cond. Dept. (for mail), General Electric Co.,
570 Lexington Ave., New York, and 200 Chit-
tenden Dr., Crestwood, N. Y.
LYONS, Cornelius J. (.1 1932), Sales Engr. (for
mail), Nash Engrg. Co., Wilson Ave., and 22
Haviland St., South Norwalk, Conn.
M
MACCUBBIN, Howard A. (A/ 1934), Pres., H. A.
Maccubbin, Inc., 2702 Alameda Ave., Baltimore,
Md.
MacDADE, Ambrose H. (U 1923), Sales (for
mail), Burnham Boiler Corp., S.E. Cor. 31st and
Jefferson Sts., Philadelphia, Pa., and 225 Haddon
Ave., Westmont, N. J,
MacDONALD, Donald B. (M 1930), C. A, Dun-
ham Co., 101 E. Walnut St., Kingston, Pa.
MACDONALD, Everett A. (A 1933), Br. Mgr.
(for mail), Spencer Heater Co., 145 Broadway,
Cambridge, and 154 Standish Rd., Watcrtown,
Mass.
MAGHEN, James T. (J 1934), Chicago Br. Mgr.
(for mail), The Ric-wiL Co., 'ill W. Monroe St.,
and 420 Diversey Pkwy., Chicago, 111.
MacKENZlE, John J. (M 1925), 004 Shaw St.,
Toronto, Qnt., Canada.
MacLEOD, Kenneth F. (A 1033), Mgr., Htg.
Dept., Crane Co., 4 IS) Second Ave. S., and (for
mail), 7703 First Ave. N.E., Seattle, Wash.
MAJDDUX, Oliver L. (A 1TO), Chief En«r.,
United Gas £ Fuel Co. of Hamilton, Ltd., and
(for mail), IS Whitten Rd., Hamilton, Ont.,
MADISON, Richard IX (A/ 1920), Research
Engr. (for mail), Buffalo Forge Co., 490 Broad-
way, and 133 Lisbon Ave., Buffalo, N. Y,
MAEHUNG, Leon S. (M 1932), Supervisor Sales,
Equitable Gus Co., 427 Liberty Ave., and (for
mail), 448 Sulgrave Rtl., Pittsburgh, Pa.
MAG INN, Peter F. )Ltf« Member; M 1008), Mfr«.
Agent, 1140 8. Neglcy Ave., Pittsburgh, )Pa.
M^GIHL, Willis J. (Af 10&4; A 1931: J 1027),
Chief Knar, (for mail), P. H. McGJrl Foundry &
Furnace Worka, 401-1,'i E, Oakland Ave., and 108
Warner Ave., Bloomington, III.
MAGNKY, Gottlieb R. (M 1931), Pres. (for mail),
Ma&ney & Tusler, Inc., Archts. and Kngra.,
104 S. Ninth St., and &*2U Waahburn Ave, SM
Minneapolis, Minn,
MAHONEY, David J. (M 1930; A 1926), Br,
Mgr. (for mail), Johnson Service Co., 503
Franklin St., and 90 Delham Ave., Buffalo, N. Y.
MAIER, George M. (M 1921), AssL to Vice-
Prea. and Gen.. Mgr. of Mfg., American Radiator
Co., 8007 Jos Campau, Detroit, Mich,
MAILLARP, Albert L. {M 1034). Head of Air
Cond, Div. (for mail), Kansas City Power &
Light Co., 1330 Baltimore, and 3740 Washington,
Kansas City, Mo.
MAIMAN, Herbert (J 1935; 5 1032), 70-04-78th
Ave,. Glendale, L. I., N. Y.
MAtLIS, William (M 1914), 330 Lycm BIdtf,,
Seattle, Wash.
MAJLONE, JDayte G. (M 1929; A 1925), Pres,,
Petroleum Heat & Power Co., 1725 S. Michigan
Ave*, and (for mail), 7315 Merrill Ave,, Chicago,
MALVIN, Ray C. (M 1920), Pres. (for mail),
Mfdvirt & May, Inc., 33^ S, Michigan Ave, and
8211 Ltngley Ave,, Chicago, III.
MANAHAN, James E. (.U 1934; A 1031; J li>2<>),
Air Cond. Engr., Kelvinator Div. (for mail),
Witte Hardware Co., 704 N. Third St., and
3455a Utah Ave., St. Louis, Mo.
MANDEyiLLE, Edgar W. (M 1914), 1171 East
37th St., Brooklyn, N. Y.
MANN, Leo B. (J 1030), Air Cond. Engr. (for
mail), Carrier Ensrg. Corp., 12 South 12th St.,
Philadelphia, and 3018 Garrctt Rd., Drcxcl
Hill, Pa.
MANNING, Walter M. (M 1930), I Its. Kn«r.,
Salesman, Crane Co., 115 K. Front ,fcst., Grand
Island, and (for mail), P. O. Box 112, Clarks,
Nebr.
MARINO, Dominic A. (J 1035; S 1033), 755 Kast
210th St., New York, N. Y.
MARKS, Alexander A. (A 1030), Awst. Sales MKr.
(for mail), Richmond Radiator Co., 2241 N.
American St., and GG35 McCallum St., Phila-
delphia, Pa.
MARKUSII, Emory U. (,U 1031), Mcch Kn«r.,
Consulting Eni>r. (for mail), 225 Kast 21st St.,
New York, and S442~85th Rd,, Wooclhaven,
L. L, N. Y.
MARRINER, John M. S. (H 103 n, Sales Kn«r.,
John Intflis & Co., Ltd., 14 St radian Ave., and
(for mail) HIM Balsam Ave., Toronto, Out.,
Canada.
MARSGHALL, Peter J. (M l'J30; A 15)30;
J 1927), Engr., Krocschell En«r«, Co., 23()(i
N. Knox Ave,, and (for mail), 2201 TouUy Ave.,
Chicago, 111.
MARSHALL, IL Hall (M 1923), 37 West 43rd
St., New York, N. Y.
MARTENIS, John V. (M 1018), Associate Prof.,
University of Minnesota, and (for mail), 4SOO
Bloomington Ave., Minneapolis, Minn,
MARTIN, Albert B. (.U 11H7K Kewaneo Boiler
Co., Inc., 1S5S S. Western Ave., ChU'UK»», 111.
MARTIN, George W.* (At 11)11), SupervimnR
ICngr, (for mail), U. S. Realty ^ Improvement
Co., Ill Broadway, New York, N, V., ami 340
Prospect St., Ridgevvood, N. J.
MARTINEZ, Juan J. (J iWitt), P.tseo de la
Reforma 183, Mexico, 1), F,
MART1NKA, Paul I>. (S 1U34), 13703 Cliau-
taugua Ave., Cleveland, Ohio,
MARTOCEtLO, Joseph A, (M 11)34), Prea.,
j. A. Martocello & Co., aai) North 13th St.,
Philadelphia, Pa.
MARTY, Ed^ar O. (M 1016), Ptes. utul Gen.
M^r., Indian Head Anthracite, Inc., and (for
mail), 1775 Howard Ave., Pottsville, Pa.
MARUM, Otto (M 1931), Plant Engr,, Agfa
Anaco Corp., 21) Oharlca St., un<l (for nmil), 12
Grand Blvd., Bingfaamton, N. Y.
MATCHETT, James O, (M 1923), Vlre-Pres. tmd
Gen. IVIgr. (for mail), Illinois Engri, ("o,, iilst
and Rucinf Ave., and 9930 JS. Winchester Avt*.,
Chicago, HI,
MATHER, Harry H, (A I03U), PhiladelphiH-
Klectric Co., 1000 Chestnut St., Phil«dplphla, Pa.
MATHEY, Nicholas J. (Af U)lf»)» Mathcy Plbg,
& Htg, Co., 31 Third Ave, N,W«, I,c Mars, I own.
MATHIS» Euftene* (M 1922), New York Blower
Co., 32nd St. and Shields Av#,, Armour P. O.
Station, Chicago, 111,
MATHIS, Henry (M 1921), The New York
Blower Co,, 32nd and Shields Ave., and (for
mail), 10317 Oakley Ave., Chicago, HI.
MATHKS, Jfuliim W. (A 1021), New York Blower
Co., 32nd St. and Shields Ave,, Chicago. Ill,
MATHLS, Victor John (J 1035; S 1033), 11307 S,
Longwood Dr., Chicago, III.
MATTHEWS, John B, (M WB4), DJgt, Mgr.,
B. F, Sturtcvant Co., 1108 Commerce Bldg,» and
(for mail), 5042 Lydia St., Kansas City, Mo,
MAT&BISL Harry B* (M 1919), Vica-Pwi, (for
mail), Carrier BJngrg, Corp,, $00 Unloa Trust
Bldg,, Cleveland, and 8lft Chadboume Bd*.
Shaker Heights, Ohio,
MATtlttO. Joseph R. (J
North 13th St., Newark, N,
ROLL OF MEMBERSHIP
MAUER, William J.i: (M 1919), Sales Mgr., Unit
Heater Div. (for mail), C. A. Dunham Co., 450
E. Ohio St., Chicago, and 2525 Colfax St.,
Evanston, 111.
MAUTSCH, Robert (.1 1028), Engr., Managing
Director (for mail), Compagnie Beige Des
Freins Westinghouse 97, Avenue Louise, 'and
Avenue des Klauwaerts 38, Brussels, Belgium.
MAWBY, Pensyl (M 1934), Service Engr.,
Lehigh Navigation Coal Co., 143 Liberty St.,
New York, N. Y., and (for mail), 312 Swarth-
more Ave., Ridley Park, Pa.
MAXWFXL, George W. (J 1935; 5 1932), Supt.
and Engr., Kenealy & Maxwell, Main St., P, O.
Box 447, and (for mail), P. O. Box 422, Harwich
Port, Mass.
MAY, Clarence W, (M 1938), Pres. (for mail),
May & Griffin, Inc., 501 Orpheum Bldg., and
2457 Sixth Ave. W., Seattle, Wash.
MAY, Edward M. (M 1931), Combustioneer, Inc.,
1835 S. Michigan Ave., Chicago, and (for mail),
1022 N. Hayes Ave., Oak Park, 111.
MAY, George Elmer (M 1933), Air Cond, Engr.
(for mail), New Orleans Public Service, Inc.,
317 Buronne St.. and 2031 Short St., New
Orleans, La.
MAY, Maxwell F. (M 1929), Secy-Treas. (for
mail), Malvin & May, Inc., 332 S. Michigan
Ave., Chicago, and Palos Park, 111.
MAYETTK, Charles E, (A/ 1926), 1400 Floral St.
Washington, D. C.
MAYNARD, Herbert R. (5 1935), 1725 Wood-
land Ave., Duluth, and (for mail), 1014 Seventh
St. S.K., Minneapolis, Minn.
MAYNARD, J. Earle (M 1931), Chief Htg.
Knur,, Fox Furnace Co., and (for mail), Tele-
graph Rtl., Elyria, Ohio.
McCAULEY, James II. (M 1921), James H.
McCaulcy, Inc., 5321 West 05th St., Chicago, III.
McCLKLLAN, James E. (M 1922), Mgr., Chicago
Dist. (for mail), American Blower Corp., 228 N,
LaSalle St., Chicago, and 88M LaCrosse Ave.,
Nilea Center, 111.
McCLINTOCK, Alexander, Jr. (M 1928; J 1920),
Member of Firm (for mail), A. McClmtock &
Sons, 11)37 Ridge Ave., and 121 Rochclle Ave.,
Wiaaahickon, Philadelphia, Pa.
McOLOUGlIAN, Charles (S 1934), 279 Ryeraon
St., Brooklyn, N, Y.
McOOLL, Jay R,* (M 1910), (Presidential
Mmbf.r'), (Pros., 1922; 1st Vice-Pros., 1021; 2nd
Vicc-Prt'8,, 11)20; Council, 1920-1023), 2304
Penobscot Bldg,, Detroit, Mich.
McCONACUIB, Lorn* L. (A 1028) > Htg. and
Plbg., 8817 Mack Ave., ami (for mail), 1379
Maryland Ave.» Detroit, Mich.
McCQNNER, Charles R. (A 1925; J 1922), Gen.
Salea Mgr. (for mail), Clanigc Fan Co., and 1904
Waite Ave., Kalamazoo, Mich,
McGORMAGK, Denis (M 1933), Mgr., Air
Cond. Instruments and Control Dept. (for mail),
Jullen P. Kriez & Sons, Inc., 4 N. Central Ave.,
and 5924 Hellona Ava., Baltimore, Md.
McGOY, Thomas F, (M 1924), Mgr. (for mail),
The Powers Regulator Co., 125 at, Botolph St.,
Boston, and Glen Rd,, Wellealey Farms, Mass.
McGREERY, Hufth J, (U 1022), (for mail),
Marine Bldg., and 1617-49tli Ave, W,, Van-
couver, B« C,» Canada.
McGtJNE, Byron, V. (M 1928), Sties Engr. (for
mall), 101 W, Yaklma Ave., P. O, Box 385, and
2810 W. Yaktmt Ave,, Yakima, Wash.
McDONALP, Thomas (A 1031), Mgr, (for mail),
Minneapolis-Honeywell Regulator Co,, Ltd.,
H7 Peter St., and $(J ICingsway, Toronto, Out.,
Canada*
HeJ>QtoBIX» Everett N, (M 1023), Prea. (for
"" ( McDonnell IE Miller, 400 R Michigan
and 105 E, Delaware, Chicago, 111. ^
3IN, Joto W* (7 1981), 180 Rowland Park,
F. (A 1928), 1258 Pratt
Mi, Smith ft MoOinn^e Co., 527 JWwt
n and 142 Btllleld Ave*, Pittsburgh, Pa,
McGLENN, G. Raymond (M 1915), 259 Lormore
St., Elmira, N. Y.
McGONAGLE, Arthur (M 1932), Consulting
Engr. (for mail), 1013 Fulton Bldg., Pittsburgh,
and 6815 Prospect Ave., Ben Avon, Pa.
McGRAIL, Thomas E. (M 1926), Mgr. Htg.
Dept., Crane, Ltd., Beaver Hall, and (for mail),
W. A. 90S7-34G5 Belmore Ave., Montreal, P. Q.,
Canada. "
McGUIGAN, L. A. (A 1919), 724 Hastings St.,
Pittsburgh, Pa.
McHENRY, Robert W. (M 1921), Engr., Trans.
Canada Radiator & Boiler Co., 672 Dupont St.,
and (for mail), 236 Eglinton Ave., Toronto, Ont.,
Canada.
MclLVAINE, John H.* (A/ 1029), Prcs. (for mail),
McIIvaine Burner Corp., OG3 W. Washington
Blvd., and 1100 Lake Shore Dr., Chicago, 111.
MclNTIRE, James F. (M 1915; A 1914), (Coun-
cil, 192G-192S, 1932-1934), Vice-Pres. (for mail),
U. S. Radiator Corp., 1056-44 Cadillac Square,
P. O. Box 686, and 3261 Sherbourne Rd., Detroit,
Mich.
McINTOSH, Fabian C. (Al 1921; J 1917),
(Treas., 1930; Council, 1929-1934), Br. Mgr. (for
mail), Johnson Service Co., 1238 Brighton Rd,,
and 302 Marshall Ave., Pittsburgh, Pa.
McKIEVER, William H.* (M 1897; J 1896),
Pres. (for mail), William H. McKiever, Inc., 247
West 13th St., New York, and 479 Eighth St.,
Brooklyn, N. Y,
McKINLEY, C. B. (5 1934), 132 Paye, Norman,
Okla.
McKINNEY, William J. (.1 1934), Mgr., Atlantic
Dist., American Blower Corp., 710-101 Marietta
St. Bldg., Atlanta, Ga.
McKOTRICK, Percy A. (A 1934), Treas. and
Gen. Mgr. (for mail), Parks-Cramer Co., 970
Main St., and 219 Blossom St., Fitchburg, Mass.
McLARNEY, Harry W. (M 1933), Air Cond.
Engr. (for mail), Union Electric Light & Power
Co., 315 North 12th St., and 5053 Lindcnwood
Ave., St. Louis, Mo.
MCLAUGHLIN, Joseph D. (A 1930; J loss),
Owner (for mail), Bralcy & McLaughlin, 166
Aborn St., and 45 Roslyn Ave.» Providence, R. I,
McLEAN, Dcrmld (M 1917), McColl, Snyder c%
McLean, 2304 Penobscot Bldg., Detroit, Mich.
McLEISH, William S. (A 1932: J 1928), Dist.
Engr. (for mail), The Ric-wiL Co., Room 1838,
101 Park Ave., and 500 Riverside Dr., Ne'w
York, N. Y.
McLENEGAN, David W. (M 1933), Asst. Engr.,
Air Cond. Dept. (for mail), General Electric Co.,
1 River Rd., and 16SG Rugby Rd., Schenectady,
N. Y.
McLOUTH, Bruce F. (J 1934), Dail Steel
Products Co., Lansing, Mich.
McMAHON, Thomas W. (M 1928), Dist, Mgr.
(for mail), American Blower Corp., 1715 Railway
Exchange Bldg., and 0151 Waterman Ave.,
St. Louis, Mo,
McMUNN, A. H, (S 1934), (for mail), 4915
Forbes St., Pittsburgh, Pa., and 311 St. Clair St.,
Cl&rkuburg, W. Va.
McMURRER, Louis J. (M 1928: A 1928 ; J 1924),
Pres., The McMurrer Co,, 303 Congress St,,
Boston, and (for mail), 190 Harvard Circle,
Newtonvllle, Mass.
McNAMARA, William (A 1030), Sales Engr. (for
mail), The Trane Co,, 2694 University Ave., and
1855 Como Ave* W,, St. Paul, Minn.
McPHERSON, William A. (M 1929), Chief,
Htg, and Vtg. Div., Dept, of School Bldgs., H
Beacon St., Boston, and (for mail), 86 Dwinnell
St» West Roxbury, Mass.
McOUAlD, Dan J. (M 1934), Engrg. Service
Work, 1505 Milwaukee St., Denver, Colo,
McTERNAN, Felix J, (A 1981), 1523 Main St.,
Buffalo, N, Y,
MKADt Bd<ward A. (M 1$26>, Asst Sales Mgr. (for
mail), Nash Engrg. Co., and 5 Thames St.,
Norwalk, Conn.
27
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
MEFFERT, George H. (7 1930), Engr. (for mail),
Carrier Engrg. Corp., 2022 Bryan St., and 41543^
Prescott Ave., Dallas, Texas.
MEHNE, Carl A. (M 1929), Htg. and Vtg.
Expert (for mail), Room 821, 101 Park Ave.,
New York, and Livingston St., Valhalla, N. Y.
MEINKE, Howard G. (M 1933), Asst. Engr.,
Civil Engrg. Dept. (for mail) , New York Edison
Co., 4 Irving PL, Room 1517-S, New York, and
41 Harte St., Baldwin, Nassau Co., N. Y.
MEISEL, Carl L. (J 1931), 350 Central Park West,
New York, N. Y.
MELLON, James T. J. (M 1911), (Council,
1915), (for mail), Mellon Co., 4415-21 Ludlow
St., and 431 North 63rd St., Philadelphia, Pa.
MENSING, Frederick D. (M 1920), (Treas.,
1931-1932; Council, 1931-1932), Consulting Engr.
(for mail), Mensing & Co., 12 South 12th St.,
and 2845 Frankford Ave., Philadelphia, Pa.
MERKEL, Fred P. (M 1924), 204-llth Ave.,
Belmar, N. J.
MERLE, AndrS (M 1934), Director of Engrg.,
Control Corp. ot America, 250 West 57th St.,
New York, N. Y., and (for mail), 172 Lincoln
Ave., Elizabeth, N. T.
MERRILL, Carle J. (M 1919), Treas. (for mail),
C. J. Merrill, Inc., 54 St. John St., and 15
Longfellow St., Portland, Maine.
MERRILL, Frank A. (M 1934), Consulting Htg.
and Vtg. Engr. (for mail), Hollis French, 210
South St., Boston, and 19 Auburndale Rd.,
Marblehead, Mass.
MERRITT, G, J. (M 1925), Director, Merritt,
Ltd., 8 French Bund, Shanghai, China.
MERTZ, Walter A. (M 1919), Kehm Bros, 51 E.
Grand Ave., Chicago, 111.
MERWIN, Gile E. (M 1924; J 1923), Secy.,
Rockford Plbg. Supply Co., and (for mail),
1325~20th St. Rockforcl, 111.
MEYER, Charles L. (M 1930), 198-25 Foothill
Terrace, Hollis, L. I., N. Y.
MEYER, Frank L. (M 1932; J 1928), Viee-Pres..
The Meyer Furnace Co,, and (for mail), i) Cole
Court, Peoria, 111.
MEYER, Henry C., Jr.* (M 1898), (Council,
1915-1916), Pres. (for mail), Meyer Strong &
Jones, Inc., 101 Park Ave., New York, N. Y., and
25 Highland Ave., Montclair, N. J.
MEYER, John W. (A 1929), Asst. to Mgr.,
Industrial Sales Dcpt. (for mail), Philadelphia
Electric Co., 1000 Chestnut St., and 5000 Pine
St., Philadelphia, Pa.
MICHIE, IX Fraser (A 1930), Boiler and Rad.
Div., Crane, Ltd., &J Lombard St., and (for
mail), 5 B, 553 Wardlaw Ave., Winnipeg, Man,,
Canada.
MILES, James C. (M 1914), Dept. Mgr. (for
mail), The Henry Furnace & Foundry Co.,
3471 East 49th St., and 1803 Crawford Rd.,
Cleveland, Ohio,
MILLAR, Rowland J. (M 1925), Mgr. (for mail).
Pease Foundry Co,, Ltd., 118 King St. K,, and
S,?Oakmount Rd, Toronto, Ont,, Canada.
MILLARD, Jimius W, (HI 1929), Diet. M«r. (for
mail), Carrier Engrg. Corp., 410 Asylum St.,
Hartford, and Manchester, Conn.
MILLER, Bruce R. (A 1930), 1533 N.W. 25th St.,
Oklahoma City, Okla,
MILLER, Charles A. (A I«17), Salesman (for
mail). The H. B. Smith Co., 10 East 41st St., and
2870 Marion Ave., New York, N. Y,
MILLER, Charles W. (M 1919; J 1908), (for
mail), The Rado Co., 388 S. Second St., Mil-
waukee, and R, 1, Box 42, Menomonee Falls,
Wta.
MILLER, Floyd A, (M 1011), 477 Federal Bldg.,
Chicago, 111.
MILLER, Harold A, (S 1935), 1000-24th Ave,
S,E,» Minneapolis, Minn.
MILLER, Harry M, (M 1920), 3938 N. Stowell
Ave., Milwaukee, Wis.
MILLER, James E. (M 1914; J 1912), Vice-Prea,
(for mall), C. W, Johnson, Inc., 2>11 N. Des-
plainea St., Chicago, and 2210 Colfax St.,
Evanston, III,
MILLER, John F. G. (M 1916), Vice-Prcs. (for
mail), B. F. Sturtevant Co., Hyde Park, Boston,
and 20 Chapel St., Brookline, Mass.
MILLER, Leo B. (M 1926), Refrigeration Div. (for
mail), Minneapolis-Honeywell Regulator Co.,
2753 Fourth Aye. S., and 2010 James Ave, S.,
Minneapolis, Minn.
MILLER, Lorin G. (M 1933), Prof. Mech. Engrg.
(for mail), Dept. of Mech. Engrg., Michigan
State College, Engrg. Bldg., and 920 Sunset
Lane, E. Lansing, Mich.
MILLER, Merl W. (M 1932; J 1920), Mgr. of
Lab. (for mail), Trane Co., and 229 South St.,
LaCrosse, Wis.
MILLER, Robert A.* (M 1931), Tech. Sales Engr.
(for mail), Pittsburgh Plate Glass Co., 2200
Grant Bldg., Pittsburgh, and 1211 Carlisle St.,
Tarentum, Pa.
MILLER, Robert T. (A 1927), Chief Engr. (for
mail), Masonite Corp., Ill W. Washington St.,
Chicago, and 1228 Sunnyside Ave., Chicago
Heights, 111.
MILLER, Tolbert G. (A 1929; J 1921), Supt.,
Htg. and Vtg., 11 N. Second St., Wormleysburg,
Pa.
MILLIKEN, James H.* (M 1923), Dist. Repr.
(for mail), American Air Filter Co., Inc., 20 N.
Wacker Drive, Chicago, and 1021 Ridge Ct.,
Evanston, 111.
MILLIKEN, Vincent D. (A 1930), Sales Mgr. (for
mail), Skidmore Corp., and 2015 Forres Ave.,
St. Joseph, Mich.
MILLIS, Lirm W. (Life Member; M 1018), Secy.,
Security Stove & Mfg. Co., 1U30 Oakland, and
(for mail), 3534 Wabaah Ave,, Kansas City, Mo,
MILWARD, Robert K. (A 1920), Mgr. (for mail),
U. S. Radiator Corp., 127 Campbell Ave., and
2441 Culvert Ave., Detroit. Mich.
MINER, Major H. (,S 1934), 1510^ North-wuat 25,
Oklahoma City, Okla.
MITCHELL, C. II. (A/ 1924), Engr., The Fels Co.,
42 Union St., Portland, Maine, and (for mail),
179 Thatcher St., Milton, Mass.
MITTENDORFF, E. M. (M 1932), Sules Engr.,
ffor mail), Sarco Co., Inc., 222 N. Bank Dr.,
Chicago, and 1000 S. Prospect Ave., Park Ridge,
III. '
MJOLSNES, Leonard O. (S 1035), 018 15th
Ave. S.K., Minneapolis, Minn.
MOOIANO, Rene (M 1925), 55 Boulevard Beau-
sejour, Paris, 10, erne, France.
MOLER, William H, (Af 1927; J 1923), Bn
Supervisor Com. Div., York Ice Machinery
Corp., 2225 S. Lamar St., Dallas, ami (for mail),
R. K, D. 1, Box 37B, Irving, Texas.
MONDAY, Charles E. (M 1920), Chas, E,
Monday & Co., 1328 Fairmount Ave., Phila-
delphia, Pa.
MONROE, Meade (J 1035; S 1933), 1228 Southern
Blvd., New York, N. Y.
MONROE, Raymond R, (A 1929), 7 County St.,
Ipawich, Mass.
MONTGOMERY, Ora C, (M 1933), Asst. Supt.
of Power (for mail), N. Y. C, R, R., Grand
Central Terminal, Room 1$4#» and 255 West
84th St., New York, N, Y,
MOODY, Lawrence E, (M 1919), Member of
Firm, Isaac Hathaway Francis, Consulting
EnKra., Otis Bldg., Philadelphia, Pa,» and (for
mail), 237 Jefferson Ave., Haddonfteld. N. J.
MOON, L. Walter (M 1915), (Council, 1933-
1034), Pres, (for mail), Bradley Heating Co.,
3884 Olive St., and 5006 N. Kingshigkwty,
St. Louis, Mo.
MOORE, Henry W* (M 1935), Mr Cond, Engr.
(for mail), Frigldalre Corp», Dayton, Ohio, and
«16 Greenland Dr., Murfre^sboro, Term.
MOORE, Herbert S. (A I923)» Mfr». Agent, 107
Clendenan Ave., Toronto 0> Ont., Canada*
MOORE, Robert E* (J 1933), Junior Sale* Bn«r,
(Div, of), Manning Mwcweu & Moore, 446
Communlpaw Ave,, Jersey City, N. J,» a»d (for
mail), 1730 Bast 46th St., Brooklyn, N. Y»
MOORB, Robert B. (A 1928), 714 Brumwel SU
Evanston, 111.
28
ROLL OF MEMBERSHIP
MOREAU, Donate (-4 1932), 35 E. McCormick,
Tucson, Ariz.
MORGAN, Glenn C. (M 1911), Partner (for mail),
Morgan-Gerrish Co., 307 Essex Bldg., and 4308
Fremont Ave. S., Minneapolis, Minn!
MORGAN, Robert C. (M 1915), 314 W. Seymour
St., Philadelphia, Pa.
MOREHOUSE, H. Preston (M 1933), General
Air Cond. Repr. (for mail), Public Service Elec.
& Gas Co., 80 Park PL, Newark, and S5 Halsted
St., East Orange, N. J.
MORRIS, Arnold M. (J 1934), Sheet Metal
Worker, Philadelphia Navy Yard, Sheet Metal
Shop Building No. 17, and (for mail), 3022 Baltz
St., Philadelphia, Pa.
MORRIS, Edward J. (7 1935; 5 1931), Engr.,
Morris Engrg. Co., Inc., 107 E. Pleasant, and
(for mail), 3414 Gwynn's Falls Pkwy., Balti-
more, Md.
MORRIS, Fred H. (A 1929), 14704 Stratmore
Ave., E. Cleveland, Ohio.
MORRISON, Chester B. (M 1931), Mgr. (for
mail), York Shipley Co., 81 Jinkee Rd., and
347 Route Cohen, Shanghai, China.
MORSE, Clark T. (M 1913), Pres. (for mail),
American Blower Corp., 6000 Russell, and
16222 Shaftsbury Rd., Detroit, Mich.
MORSE, Floyd W. (A 1934), (for mail), Chamber-
lin Metal Weather Strip Co., 52 Vanderbilt Ave.,
New York, and 112 Sycamore Ave., Mt. Vernon,
N. Y.
MORTON, Charles H. (A 1931), HOG Sherman
St, S.E., Grand Rapids, Mich.
MORTON, Harold S. (M 1931), Dist. 'Mgr.,
Modern Coal Burner Co., 538 Baker Bldg., and
(for mail), 4330 Wooddale Ave., Minneapolis,
Minn,
MOSHBR, Clarence H. (A 1919), C. H. Mosher
Co., 423 Ashland Ave., Buffalo, N. Y.
MOSS, Edward (M 1920), 1130 Atlantic Ave.,
Brooklyn, N. Y.
MOTZ, O. Wayne (M 1932), Mech. Engr,,
Samuel Hannuford & Sons, Archts-, 1024 Dixie
Terminal Bldg., Cincinnati, and (for mail), 2587
Irving PL, Norwood, Ohio.
MOULDER, Albert W.* (M 1917), Mgr., Htg.,
Power and Industrial Piping Div. (for mail),
Grinnell Co., Inc., 260 W. Exchange St., and 12
Blackstone Blvd., Providence, R, L
MOULTON, David (M 1920), 99 Chauncy St.,
Boston, Masa.
MUELLER, Harold C* (A 1930), Sales Engr. (for
mail), Powers Regulator Co., 2720 Greenview
Ave»» Chicago, and 2720 Lawndale Ave,, Evans-
ton, IU.
MUNDER, John F., Jr. (M 1927; J 1024), (for
mail), Quinn Engrg, Co., 501 Madron Ave.,
New York, N, Y., and 81 Joyce Rd,, Tenafly,
MUNIBtL Leon L. (M 1910; J 1916), Pres, (for
mall), Wolff & Munier, Inc.. 222 East 41st St.,
New York, and 63 Columbia Ave,, Hartsdale,
N. Y,
MUNEO, Edward A. (Charter Member; Life
Member}, Htg, and Vtg. Engr,, c/o Arthur B.
Munro, 50 Jarvls PL, Lynbrook, L, L, N. Y.
MURPHY, Charles G. (S 1984), 3415 Fort
Independence St., New York, N* Y .
M0RPHY, Edward T** (M 1915), Vice-Pres. (for
mall). Carrier Engrg, Corp., 180 N, Michigan
Ave,, and 200 E. Chestnut St., Chicago, 111,
M0RPHY, Howard 0,* <M 1928), Vice-Prea. (for
mail), American Air Filter Co., me*, 215 Central
Ave*, and 4W Ughtfoot Rd,, Louisville, Ky.
MOTJPHY, Joaepfe R. (M 1034J A 1925), The
Terrace, Riverside, Conn.
MtWHY, William W, (M 1980), Trees, (for
mall). W. W. Murohy Co*, 171 Chestnut St., and
m Mansfield St., Springfield, Ma«u
MURRAY* John J, (A 1938), Salesman, Vice-
Pjres>t Pierre Perry Co,, 236 Congress St*, Boston,
and (for mail), 00 Commonwealth Park W.,
Newton Center, Mass,
MURRAY, Thomas F. (M 1923), State Architect,
14 S. Lake Ave., Albany, N. Y.
MUSGRAVE, Merrill N. (A 1935), Pres. (for
mail), Harrison Sales Co., 314 Ninth Ave. N., and
140 East 64th St., Seattle, Wash.
MYERS, Frank L. (M 1933), Sales Engr., Owens,
Illinois Glass Co., and (for mail), 3406 Detroit
Ave., Toledo, Ohio.
MYERS, Charles R. (S 1935), White Bear Lake,
R. No. 2, Minneapolis, Minn.
MYERS, George W. F. (M 1930; A 1928; J 1923),
Mfrs. Repr., Htg., Vtg., and Air Cond., Mart
Bldg., 401 South 12th St., St. Louis, and (for
mail), 476 Pasadena Ave., Webster Groves, Mo.
N
NAROWETZ, Louis L., Jr. (M 1929; A 1912),
Secy, (for mail), Narowetz Htg & Vtg. Co.,
1711 Maypole Ave., Chicago, and 112 S. Park
Ave., Park Ridge, 111.
NASON, George L. (M 1929; A 1929; J 1927), 31
N. Franklin St., Holbrook, Mass.
NASS, Arthur F. (M 1927), Secy-Treas. (for
mail), McGinness, Smith & McGinness Co., 527
First Ave., Pittsburgh, and Elmhurst Rd.,
R. P. No. 8, Crafton P. O., Pa.
NATKIN, Benjamin* (M 1909; J 1907), Pres. (for
mail), Natkin & Co*, 2020 Wyandotte, and 5211
Rockhill Rd.. Kansas City, Mo.
NAYLOR, Charles L. (M 1931), Supt., Heat,
Light and Power (for mail), The Atlantic
Refining Co., 3144 Passyunk Ave., and 2315
North ISth St., Philadelphia, Pa.
NEALE, Laurence I. (A 1927), Vice-Pres, (for
mail), Atlantic Gypsum Products Co., 60 East
42nd St., and 125 East 57th St., New York, N. Y.
NEARY, Daniel A. (J 1935; 5 1933), 444 East
66th St., New York, N. Y.
NEEDLER, J. H. (M 1933), Phillips Getschow
Co., 32 W. Austin Ave., Chicago, 111.
NEILER, Samuel G. (M 1898). Consulting Mech.
and Elec. Engr. (for mail), Neiler, Rich & Co.,
431 S. Dearborn St., Chicago, and 737 N. Oak
Park Ave., Oak Park, 111.
NELSON, Chester L. (/ 1929), 6704 Oconto
Ave. N., Chicago, 111.
NELSON, D. W,* (M 1928), Asst. Prof, of Steam
and Gas Engrg. (for mail), Mech. Engrg. Bldg.,
University of Wisconsin, and 3906 Council
Crest, Madiaon, Wis.
NELSON, George O. (M 1923), Carstens Bros.,
Ackley, Iowa.
NELSON, Harold A. (M 1926), 236 S. La Pere St.,
Beverly Hills, Calif.
NELSON, Herman W. (M 1909), Pres. and Gen
Mgr. (for mall), The Herman Nelson Corp., 1824
Third Ave,, and 2500-llth St., Moline, 111.
NELSON, Raymond Allen (S 1935), 14th St. and
Prospect Ave,, Cloquet, ana (for mail), 418-18th
Ave. S.E., Minneapolis, Minn.
NELSON, Richard H, (A 1033; J 1928), Secy-
Treas,. Herman Nelson Corp., 1824 Third Ave.,
and (for mail), 1303«30th St., Moline, 111.
NESBITTj Albert J,* (M 1921; J 1921), Secy-
Treas, (for mail), John J. Nesbitt, Inc., State
Rd, and Rhawn St., and Matchwood Apts*,
Wissahickon Ave., and School Lane, Phila-
delphia, Pa,
NESBITTf John J. (M 1923), John J, Nesbitt,
Inc., State Rd. and Rhawn St., Holmesburg,
Philadelphia, Pa.
NESDAHL, Eilett (M 1915), c/o Colben Nesdahl,
Route it Shevlin, Minn4
NBSS, William H. G, (M 1931), Gen. Mgr, (for
mail), Master Fan Corp., 1323 Channing St., and
215 N, Kingaley Dr,, Los Angeles, Calif.
NESSI, A*idr6 (M 1930), Ingr des Arts et Manu-
factures, Expert prea. le triblnal civil de la Seine,
and (for mail), 1 Avenue du President Wilson,
Paris XVI, France,
NBU, Henri J. E. (M 1933), Pres,, Etablissements
Neu, 4.7-49 Rue Fourier, Lille (Nord), France.
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
NEWCOMB, Lionel B. (J 1933), Junior Engr.,
Philadelphia Electric Co., and (for mail), 6056
Walton Ave., Philadelphia, Pa.
NEWPORT, Charles F.* (U 1900), Sales Engr.,
Weil-McLain Co., Michigan City, Ind., and (for
mail), ,10001 Longwood Dr., Chicago, 111.
NICELY, John E. (A 1925), 120S Marion St.,
Reading, Pa.
NICHOLLS, Percy* (M 1920), Supervising Engr.,
Fuel Section (for mail), U. S. Bureau of Mines,
Pittsburgh, Pa.
NIGHTINGALE, George F. (A 1931), Western
Sales Mgr., Tuttle & Bailey, Inc., 61 W. Kwizie
St., Chicago, and (for mail), 621 S. Maple Ave.,
Oak Park, 111.
NOBBS, Walter W. (M 1919), 50 Fairhazcl
Gardens, London N.W.6, England.
NOBIS, Harry M. (M 1914), 1827 Stanwood Rd.,
East Cleveland, Ohio.
NOBLE, Theodore G. (J 1935; S 1933), Ensr.,
Minneapolis Gas Light Co., and (for mail), 523
Oak St. S.E., Minneapolis, Minn.
NOLL, William F. (M 1924), Htg. Contractor,
2850 North 47th St., Milwaukee, Wis.
NORDHEIMER, Clyde L. (/ 1935; S 1931), 622
Mellon St., Pittsburgh, Pa.
NORRIS, William D, (M 1930), 1314 Forest
Ave., Wilraette, 111.
NORTHON, Louis (AT 1929), Consulting Engr.,
132 Park Ave., Mt. Vernon, N. V.
NOTTBERG, Gustav (A 1033), Secy, (for mail),
U. S. Engineering Co., 914 Campbell, and 1835
East 68th St. Terrace, Kansas City, Mo.
NOTTBERG, Henry (M 1919), Vice-Pres. (for
mail), U. S, Engineering Co., 014 Campbell St.,
and 213 South Bales, Kansas City, Mo.
NOVOTNEY, Thomas A. (M 1928), Mgr.,
Research and Sales Engrg, Depts., National
Radiator Corp., 221 Central Ave., and (far mail),
403 Wayne St., Johnstown, Pa.
NOWITSKY, Herman S. (A 1931), Supt., Con-
struction, Repairs and Maintenance, Wilmers &
Vincent Corp., and (for mail), 151 Tenth St.,
Norfolk, Va.
NUSBAUM, Lee* (M 1915), Owner (for mail),
Pennsylvania Engrg. Co., 1119-21 N. Howard
St, Philadelphia, and 315 Carpenter Lane,
Germantown, Philadelphia, Pa,
OAKEY, William E. (M 1932), Consulting Kngr.,
Oriakany, N. Y.
OAKS, Orion 0. (M 1917), Executive B:ngr.t
American Radiator Co., 40 West 40th St., New
York, N, Y., and (for mail), 119 Oak Ridge Ave.,
Summit, N. J-
GATES, Walter A, (M 1931), Htg. and Industrial
Engr., Lynn Gas & Electric Co., 90 Exchange
St., and (far mail), 28& Lynn Shore Dr., Lynn,
Mass.
O'BANNON, Lester $.* (M 1028), University of
Kentucky, Lexington, Ky,
OBERGv Harry C. (A JTO), Mgr,, Kngrg, Dept.f
Crane Co,, Fifth and Broadway, and (for mail),
1362 W. Minnehaha St., St, Paul, Minn.
OBERT, Caflln W.* (M 1C16), Consulting Engr.,
Union Carbide & Carbon Research Laboratories, •
IRC,, 30 East 42ncl St., New York, and (for mail),
m N. Columbus Ave., Mt. Vernon, N. Y.
O'BRIEN, J. H. (M 1923), 228 N. LaSalk St.,
Chicago, 111.
Q'CONNELJU Fresly M. (M 1016). Resident
En.gr.» Inspector, P. W, A., (for mail), College
Court Apts^ Pullman, Wash.
QFFUN, Ben (M 1028), Owner (for mail). B,
Often & Co.» 308 S. Dearborn St., and 1100 N.
Dearborn St., Chicago* 111,
OFFNER, Alfred J.* (M 1922), Consulting Engr.
(for mall), 189 East 53rd St, New York, and
I304Wltfa Ave,, Btechhurat, U 1., N, Y.
O'GORMAN, John S., Jr. (A 1934), Sales Engr.
(for mail), Johnson Service Co., 2142 East 10th
St., Cleveland, and 19205 Winalow Rd., Shaker
Heights, Ohio.
O'HARE, George W., Jr. J 1935; 5 1032), 201
West 72nd St., New York, N. Y.
ORE, William C. (J 1934), Air Cond. Engr. (for
mail), Sheldons, Ltd., 96 Grand Ave., Gait, and
1200 Richmond St., London, Ont., Canada.
OLCHOFF, Maurice (M 1933), Mgr., Qlchoff
Engrg. Co., 423 Dwight Eldg., and (for mail),
5341 Holmes, Kansas City, Mo.
OLSEN, Carl ton F. (A 1925; J 1920), Combustion
Engr., Kewanee Boiler Co., Inc., 1858 S. Western
Ave., and (for mail), 7914 Wabash Ave., Chicago,
111.
OLSEN, Gustav E. (M 1930), GS09 Amstel Blvd.,
Arverne, L, I., N. Y.
OLSON, Bernhard (A 1929), 122 S. Michigan
Ave., Chicago, and (for mail), 5724 N. Natoma
Ave., Norwood Park, 111.
OLSON, Gilbert E. (A/ 1930), 440 Ward Plcwy.,
Kansas City, Mo.
OLSON, Robert G. (M 1923), Sales Mgr, (for
mail), Hydraulic Coupling Corp., Harper at
Russell, and HI Putnam Ave., Detroit, Mich.
OLVANY, William J. (M 1912), Prea. (for mail),
William J. Olvany, Inc., 100 Charles St., New
York, and 109-40~71st Rd,r Forest Hills., L, I,,
N.Y.
O'NEIL, Joseph M. (A 1034), 332 Commonwealth
Ave., Springfield, Mass.
O'NEILL, James W. (M 1029; A 1927; J 1025),
Chief Engr., Trane Co, of Canada, Ltd., 439
King St, W., and (for mail), 8 Springmount Ave,,
Toronto, Canada,
O'NEILL, Peter (M 1920), Treas, (for mail),
Bartley-O'Neill Co., 240-42 Blvd. of Allies,
Pittsburgh, and 2448 Charles St. N.S., Pitta-
burgh (14), Pa.
OPPERMAN, Everett F, (J IQBfi; ti 1TO), 169
Milbank Ave,, Greenwich, Conn.
OREAR, Andrew G. (M 1930), Sales Engr. and
Mfra. Repr. (for mail), Room 501, San Fernando
Bldg,, Los Angeles, and 1015 K. Raleigh St.,
Olendale, Calif.
O'RBAR, L. H. (M 1934), Pres, (for mail),
Midwest Pibg, & Htg, Co., 2450 Blake St,, and
3033 West 37th Ave., Denver, Colo.
OSBORN, Wallace J. (A liW7), Vice-Prea,,
Keency Publishing Co,, Grand Central T«rm.
Bid*., New York, N. Y.r and (for mail), 500 Old
Post Rd,, Fairfield, Conn.
OSBORNE, Gurdon H. (M 1922), Gen, Mgr,,
The Vtg. & Blow Pipe Co,, Ltd,, 714 St, Maurice
St., Montreal, and (for mail), 836 Pratt Ave,,
Outremont, Montreal, Que., Canada,
QSBORNfc, Maurice M, (M 1925), 387 Beacon
St., Boston, Mass.
OSBURN, Richard M, (J 1035: S 1033), 2241
Sedgwicfc Ave,, New York, N. Y,
OSTERLB, William H* (M 1034), Engr. (for
mall), The West Penn Electric Co,, W Woocl St.,
Pittsburgh, and 333ft Beacon Hill Ave., Dormant,
Pa.
OSTRIN* Albert (S 1835)» 1210 Jam« N,,
Minneapolis, Minn,
OTIS, Gerald E.* (M 1022), Vie^-Pm, (for mall),
The Herman Nelson Corp., and 1921-aSrd Ave,,
Mollne, 111.
OTT, Onm W. at 1025), (Council 1984), Con*
suiting Mech. Eftgr. (for mail), 4^2 Wasbf&iton
Bldg»» and 123 S. Virgil Ave,f toi &jtgetts» Calif,
OTT, Rush C. (M ItBJ), Sdei Bagf., R«
ating Edulp, Corp., 9327 N* Meridlun St.,
napolis, Ind.
OUEUSOFF* L. S. (M 1931),
(for mail), Washtegton Ga«
St. N.W.. Washington,
St., Chevy Chase, Md*
OVWTON, Siduay H* (Jtf IW0), RMT,, K, . V.
Radiatore»,
land*
Co.
ROLL OF MEMBERSHIP
PABST, Charles S. (M 1934), Pres. and Mgr.
(for mail), Adams Engrg. Co., Inc., 55 West 42nd
St., New York, and S727-98th St., Woodhaven
L. I., N. Y.
PAETZ, Herbert E. (M 1922), Div. Sales Mgr.
(for mail), American Blower Corp., 2539 Wood-
ward Ave., and The Ward ell, Detroit, Mich.
PAGE, Harry W. (M 1923), Pres., Wisconsin
Equipment Co., 204 W. Wisconsin Ave., Mil-
waukee, and (for mail), 7927 Warren Ave.,
Wauwatoaa, Wis,
PAPPENFUS, Wilfrid G. (S 1935), 312-13th
Ave. S., St. Cloud, and (for mail), Pioneer Hall,
Minneapolis, Minn.
PARK, Clifton E). (M 1929), 22 Otis St., Need-
ham, Mass.
PARK, J. Frank (J 1930) f Salesman (for mail),
Carrier Engrg. Corp., 748 E. Washington Blvd.,
Los Angeles, and Route 3, Box 956, Modesto,
Calif.
PARKER, Philip (M 1915), 8 Middle St., Woburn,
Mass.
PARROTT, Lyle George (M 1922), Consulting
Engr., McColl, Snyder & McLean, 2308 Pen-
obscot BldK., and (for mail), 4078 Seebaldt Ave.,
Detroit, Mich.
PARSONS, Roger A. (J 1933), Sales Engr., Dail
Steel Products Co., and (for mail), 525 W. Grand
River Ave., Lansing, Mich.
PARTLAN, James W. (Life Member, M 1916),
14290 Goddard Ave,, Detroit, Mich.
PATERSON, James S.* (M 1922), Mech. Engr.
(for mail), Board of Education, 155 College St.,
and 23 Norton Ave., Toronto, Ont., Canada.
PATORNO, Sullivan A. S. (U 1923), Chief
Draftsman (for mail), Meyer, Strong & Jones,
Inc., 101 Park Ave,, and 312 East 163rd St.,
New York, N. Y,
PAUL, Donald I. (J 1932), Sales Engr. (for mail),
Gurney Foundry Co., Ltd., 4 Junction Rd., and
222 Kern Ave., Toronto, Ont., Canada.
PEACOCK, James K. (M 1921), Hoffman
Specialty Co., Inc., 500 Fifth Ave., New York,
and (for mail), 440 Fowler Ave., Pelliam Manor,
PEEBLES, John K., Jr. (A 1925; J 1924), 7
Brandon Apts., University, Va.
PBLLBR, Leonard (J 1934), Engr,, D. J. Peller
and 4209 Grove Ave., Richmond, Va,
PENNEL, Reed (J 1033) , 1335 Grand Ave., St.
Paul. Minn.
PENNOCK, William B, (M 1927), Dial. Sales
Engr,, T»n« Co, of Canada, Ltd., and (for mail),
02 Markland St., Hamilton, Ont,, Canada,
PBRINA, Arthur E, (/ 1035; 5 1933), 126 Court-
land St., Staten Island, N. Y., and (for mail),
Box 198, Carnegie Institute of Technology,
Pittsburgh, Pa.
PERKINS, Robert G. (A 1935), Sales Engr., llg
Electric Ventilating Co., Chicago, 111,, and (for
mail), 1&87 N* Parkway, Memphis, Tenn,
PBSTERPIELD, Charles H, (S 1982), Box 554,
University Station, Dept of Mech. Enarg.,
University of North Dakota, Grand Forks, N, D.
PETERS, Herbert H. (M 1080), Mar., H. H.
Peteti Heating Co., 1842 North 40th St., Mil*
.
PETERSON* SterUnflD. (A 1930), Br. Mgr, (for
mall), Johnson Service Co., 473 Colman Blag,,
and 50Bl Prince St., Seattle, Wash.
PFB1FER, Otto, Jr. (A 1035; J 1932), Bagr,.
Ralph D. Thonaai & Associates, 1200 Second
S., ftnd (for mail), 1516 Monroe St* N,E,,
olis, Minn,
, John F* (M 1980» J 1925), $46
Louisa St*, WlUtawtport, Pa.
PFUHL&R, Johxi t. (A 1926] J 1023), Plbg. and
Ht£, 000 Manor Rd., West New Brighton, S. I.,
PHILIP, WtiMfcm (M WO), 74 Battedo Am,
Toronto, Ont,, Canada,
PHILLIPS, Frederic W., Jr. (U 1921), L. J.
Mueller Furnace Co., 101 Park Ave., New York,
and (for mail), 825 East SSth St., Brooklyn, N. Y.
PHIPPS, Frederick G. (M 1930), Vice- Pres.,
Preston Phipps, Inc., 955 St. James St. W., and
(for mail), 2054 Mercier Ave., Montreal, P. Q.,
PIERCE,' Edgar D. (J 1933), Engr., Carrier
Engrg. Corp., 748 E. Washington Blvd., and (for
mail), 360 West 68th St., Los Angeles, Calif.
PIERCE, William MacL. (J 1935; S 1933),
Research (for mail), Mine Safety Appliance Co,,
Braddock, Thomas and Meade Sts., Pittsburgh,
Pa., and 31 Potter St., Melrose, Mass.
PIHLMAN, Arthur A. (M 1928), (for mail),
Consolidated Gas Co. of New York, 4 Irving PL,
New York, N. Y., and 235 Dwight St., Jersey
City, N. J.
PILLEN, Harry A. (A 1933), Mfg. Repr. (for
mail), Harry A, Pillen Co., 622 Broadway, and
2208 Crane Ave., Cincinnati, Ohio.
PINDER, Percy H. (M 1919), 366 Third Ave.,
New York, N. Y.
PINES, Sidney (M 1920), Vice-Pres. (for mail),
Natkin & Co., 2020 Wyandotte St., and 5225
Charlotte St., Kansas City, Mo.
PISON, Donate, Jr. (J 1935; S 1933), Moloiloilo,
Phillipine Islands.
PISTLER, William C. (M 1934), Mech. Engr. in
Charge of Design, Carl J. Kiefer, Consulting
Engr., 91S Schmidt Bldg,, and (for mail),
Orchard Lane and Crestview Ave., Pleasant
Ridge, Cincinnati, Ohio.
PITCHER, Lester J. (M 1929; A 1928; J 1924),
8129 Dante Ave., Chicago, 111.
PITTOCK, Louis B. (M 1930), (for mail), 429- B
Oliver Bldg., and 80 Berry St., Crafton Station,
Pittsburgh, Pa.
PIZIE, Stuart G. (A 1926), 215-17 N. Flagler Dr.,
West Palm Beach, Fla.
PLACE, Clyde R. (M 1924) , Consulting Engr. (for
mail), 420 Lexington Ave., and 333 East 57th St.,
New York, N. Y.
PLAENERT, Alfred B. (A 1933; J 1927), 1102
S. Park St., Madison, Wis,
PLASS, Charles Webster (M 1928) , 826 E, Haines
St., Philadelphia, Pa.
PLAYFAIR, George Alexander (A 1924), Mgr,
(for mail), Johnson Temperature Regulating Co.
of Canada, Ltd., 97 Jarvis St., Toronto, and West
Hill, Ont., Canada.
PLEWES, Stanley E. (M 1917), Philadelphia
Mgr, (for mail), Johnson Service Co., 2853 North
12th St., North Philadelphia Station 8, Phila-
delphia, and 309 Evergreen Rd., Jenkmtown, Pa.
PLUM, Leroy H. (M 1934), Industrial Engr.,
Minneapolia-Honerwell Regulator Co., 2240 N.
Broad St., Philadelphia, Pa., and (for mail),
216 Guilford Ave,, ColHngswood, N. J.
PLtJNKETT, John H. (M 1925), 81 Woodrow
Ave., Boston, Mass.
POEHNBR, Robert E. (M 1928), Vice-Pres-Secy,.
W. H. Johnson & Son Co., 330 E. St, Joe St., and
(for mail), 2308 Coyner Ave., Indianapolis, Ind,
POHLB, K, F. (A 1930), Vice-Pres., W. F. Hirach-
man Co., Inc., 202 East 44th St., New York,
N. Y,
POLDERMAN, Lambert H. (M 1927), Vice-
Pres. (for mail), Carrier Engrg. Corp. of Cali-
fornia, 748 E, Washington Blvd., and 3462
Lambeth St., Los Angeles, Calif.
POLLARD, Alfred L* (A 1032), Gen. Supt.,
Steam Heat Dept. (for mail), Puget Sound
Power & Light Co., 601 Electric Bldg*, and 3009
28th W., Seattle, Wash.
POPE, S. Austin (M 1917), Prea. (for mail),
William A, Pope Co., 26 N, Jefferson St.. Chicago,
and 831 Ashland Ave., River Fore&tf III,
PORTER, Herbert M. (U 1981), 65 North 17th
St.* Minneapolis, Minn.
POSEYt James (M 1,919), Consulting Enor. (for
mail), 175S Baltimore Trust Bldg., and 4005
Uberty Heights Ave., Baltimore, Md.
POTVlNt L«o J. (A 1934). Sales Bngr., Hoffman
Specialty Co,, Inc., ISO N. Wells St,, Chicago,
and (for mail), 341 Walnut St., Eimhurst, 111,
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
POUCHER, Richard C. (S 1935), 1480 Chelms-
ford St., St. Paul, Minn.
POWELL, Knox A. (J 1935; 5 1933), 1008-lSth
Ave. S.E., Minneapolis, Minn.
POWERS, Edgar G. (A 1934; / 1931), (for mail),
James A. Walsh, Inc., Architects Bldg., 17th and
Sansom Sts., Philadelphia, Pa., and 304 Crest
Ave., Haddon Heights, N. J.
POWERS, Fred I. (M 1920), Factory Repr. (for
mail), Box 324, and 605 S. Sixth Ave., Bozeman,
Mont.
POWERS, Fred W. (M 1911), Pres. and Gen.
Mgr. (for mail), The Powers Regulator Co.,
2720 Greenview Ave., and 900 Castlewood Ter-
race, Chicago, III.
POWERS, Lowell G. (J 1930), Sales Engr. (for
mail}, Carrier Engrg. Corp., 1501 Carew Tower,
Cincinnati, Ohio, and 325 W. Diamond Ave.,
Hazleton, Pa.
PRENDERGAST, James J. (S 1934), 2114
Stearns Rd., Cleveland, Ohio.
PRENTICE, Oliver J. (A 1927), (for mail), C. A.
Dunham Co., 450 E. Ohio St., and 850 Lake
Shore Dr., Chicago, 111.
PRESDEE, CHff W. (A 1920), Adv. Mgr., Heating
& Ventilating, 148 Lafayette St., New York,
N. Y.
PRICE, Charles E. (A 1933), Treas. (for mail),
Keeney Publishing Co., G N. Michigan Ave.,
Chicago, and 1151 ChatEeld Rd., Winnetka, 111.
PRICE, D. O. (M 1934), Htg. and Air Cond. Engr.,
General Steel Wares, Ltd., 199 River St., and
(for mail), 145 Eastbourne Ave., Toronto, Out,,
Canada.
PRICE, Ernest H. (J 1934; 5 1932), c/o Haff
Supply, Inc., Box 328, Riverhead, L. I., N. Y.
PRIESTER, Gayle B. (S 1934), 814 Fulton St.
S.E., Minneapolis, Minn.
PRYIBIL, Parul L. (A 1932), Partner, Hucker-
Pryibil Co., 1700 Walnut St. Philadelphia, and
(for mail), 328 E. Philellena St., Germantown,
Philadelphia, Pa.
PRYOR, Frederick L. (A/ 1913), 5 Colt St.,
Paterson, N. J.
PUNG, Donald W. (S 1935), 709 Ninth Ave. N.,
St. Cloud, and (for mail), 315-lGth Ave. S.E.,
Minneapolis, Minn.
PURCELL, Frederick C. (M 1020), Dial. Mgr.
(for mail), National Regulator Co., 2847 Grand
River Ave., and 18680 Santc Rosa Dr», Detroit,
Mich.
PURCELL, Robert E. (M 1916), 4001 Seebaldt
Ave., Detroit, Mich.
PURDY, A. K. (M 1922), Pres. (for mail), Purdy
Manaell, Ltd., 63 Albert St., and 30 Glenrose
Ave., Toronto, Ont.» Canada.
PURDY, Randall B. (A 1927), Assoc, Editor,
Power (for mail), McGraw-Hill Publishing Co.,
330 West 42nd St., New York, and 224~Q5-139th
Ave., Laurelton, L. I., N. Y.
PURINTON, Dexter J. (A 1923), Associate (for
mail), Voorhees, Gmelin & Walker, Archts,, 101
Park Ave,, New York, N, Y., and 23 Sachem
Rd., Greenwich, Conn.
PURSELL, H. E, (A/ 1919), Special Repr.,
Kewanee Boiler Corp,, Kewanee, IU.
PYLE, John W, (M 1919), Peru Htg, Co., 30 W.
Canal St., Peru, hid,
QUAY. 0. M.* (Charter Member; Life Member,*
Presidential Member), (Pres., 1900; 1st Vke-
Pres,, 18064899; 2nd Vice-Pres., 1895), 725
Eastern Ave., Belief ontaine, Ohio,
QUEER, Elmer Roy (M 1933), Research Engr.
gor mail), The Pennsylvania State College
ngrg, Experiment Station, and Arbor Way,
State College, Pa.
QUINUVAN, Lawrence P» (J 1935; 3 1933),
As8t.» Case School of Applied Science, and (for
mall), 1S7U Earl wood Rd., Cleveland, Ohio.
QUIGLEY, William J. (M 1920), 27 JCnowKoa
Ave*, Kenmore, N, Y.
QUIRK, Clinton H. (M 191<>; J 1015), Sales
Engr. (for mail1), Vento Div., American Radiator
Co., 40 West 40th St., New York, and 405 Front
St., Hempstead, L. L, N. Y.
R
RACHAL, John M. (J 1930), Mgr., Air Cond.
Dept. (for mail), Carrier-Brunswick Inter-
national, Inc., 850 Frelinghuysen Ave., Newark,
and 01 S. Mimn Ave., East Orange, N. J.
RACK, Edgar C. (U 1931), Consulting Engr.,
Johns-Manville, 22 East 40th St., New York,
N. Y., and (for mail), 2SS Park Ave., East
Orange, N. J.
RAFFES, Abraham (J 1935; 5 1932), care of
I. Pontak, 977 East 178th St., New York, N. Y.
RAINE, John J. (M 1912), Vice-Pros, (for mail),
The G. S. Blodgett Co., 190 Bank St., and Essex
Jet., V. P., Burlington, Vt.
RAINGER, Wallace F. (A 1930; J 1924), 441
Hawthorne Ave., Yonkers, N. Y.
RAISLER, Robert K, (A 1933; J 1930), Treaw.
(for mail) , Raisler Htg. Co., 329 Amsterdam Ave.,
and 25 East 77th St., New York, N. Y.
RAMSEY, Raymond F, (5 1933), 1522 Coutaht,
Lakewood, Ohio.
RANCKT Guy L. (A 1933), MRF., C. A. Dunham
Co., 3605 Laclede Ave., St. Louis, and (for mail),
472 Pasadena Ave., Webster Groves, Mo,
RANDALL, W. Clifton* (M 1928), Detroit Steel
Products Co., 2250 E. Grand Blvd., Detroit,
Mich.
RANDOLPH, Charles H. (A* 1930; ,4 1028;
J 1926), Air Cond. En«r., The Milwaukee
Electric Railway & Light Co., 217 W. Michigan
St., and (for mail), 1925 N. Prospect Ave.,
Milwaukee, Wis.
RASMUSSEN, Robert P. (fl/ 1931), Prea.
Economy Equipment Co., 0835 Weutwwth Ave.,
and (for mail), 1243 East 40th St., Chicago, lit.
RATHBUN, Perry W. (M 1033), Resident Kngr.
Inspector P. W, A., and (for mail), 1H09 North-
west 37th St., Oklahoma City, Okliu
RATHER, Max F. (M 1919), Johnson Service Co.,
2142 East 19th St., Cleveland, Ohio.
RAUH, Edward M. (S 1934), (for mail), 205 K.
Boyd, Norman and Alva, OkUi,
RAY, Lewis B. (M 1932), Frew, (fur mail), Ray
Engrg. Co., Inc., 800 Broad St., Newark, and
151 Augusta St., Irvington, N. J.
RAYMER, William F., Jr. (J 1934), Sales Kngr.
(for mail), American Blower Corp., 402 Brtmd
st,, Newark, and 50 N. Mtmn Ave., Eait Orange,
N.J.
RAYMOND, Fred L* (A 1020), PreE. (for mail),
F* L Raymond Co,, 620 W. Washington Blvd.,
Chicago, and 547 N. Keystone Ave,, River
Forest, 111.
RAYN1S, Theodore (J 1934), Ami, Supervisor,
Htg. and Vta., New York Navy Yard Central
Drafting Ofhcc, Vent. Sect., and (for mail),
8631-79th St., woodhavcn, L. L, N. Y.
READ, Robert R. (S 1034), (for mall), 1975
Taylor Rd,, East Cleveland, and 27aa Owufea
Rd,, Cuyahoga Falls, Ohio.
RECK, WUliftm E. (M 1927), Civil Engr,, The
Reck Heating Co., Ltd., Esromgade 1$, Copen-
hagen N,, ana Sundvey 10, Hdlerup, Denmark*
RBDF1&LD, Clarke (J 1935; 5 1982), 318 Hngle
St., Tenafly, N. J,
REDSTONE, Arthur L. (M 1931), Research
Engr. (for mail), Proctor 8t Schwartz Seventh
and Tabor Rd.. and Park Towers, Kmbte and
Ogonta Ave., Philadelphia, Fa.
REED, Irvij*& <3, (/ 1&34), A«at. Supt and Chief
Engr, (for mail), Grant BldK», Inc., Room 417,
310 Grant St.» and 8009 Homt Ave,, Mt. Oliver,
Pittsburgh, Pa.
REED, John F, (M 1027: A 1023), Vioa*Ptm (for
mail), American Air Filter Co,, 420 ,"
Ave,, New York, and 87 Sapmore T
vWe, N, Y,
32
ROLL OF MEMBERSHIP
REED, Paul L. (A 1932), 1034 Art Hill PI., St.
Louis, Mo.
REED, Van A., Jr. (M 1930), Mech. Engr. (for
mail), Federal Engineering Co., 239 Fourth Ave.,
Pittsburgh, and 114 Water St., Elizabeth, Pa.
REED, William M. (M 1927), American Air
Filter Co., 215 Central Ave., Louisville, Ky.
REGER, Henry P. (M 1934), Pres. and Treas. (for
mail), H. P. Reger & Co., 1501 East 72nd PL,
and 6939 Bennett Ave., Chicago, 111.
REID, Henry P. (M 1981; A 1927), Special Engr.
(for mail), Universal Atlas Cement Co., 20S S.
LaSalle St., Chicago, and 3507 Oak Park Ave.,
Berwyn, 111.
REID, Herbert F. (A 1932), Reid-Graff Plbg. Co.,
1417 Peck St., Muskegon Heights, Mich.
REIIXY, Charles E. (J 1928), 4920 City Line
Ave., Philadelphia, Pa.
REIJLLY, J. Harry (M 1931; A 1931; J 1929),
Sales Engr., American Radiator Co., 402 Broad
St., Newark, and (for mail), 14 Watson Ave.,
East Orange, N. J.
REINKE, Alfred G. (J 1933), Group Leader on
Instruments, Westinghouse Electric & Mfs. Co.,
95 Orange St., Newark, and (for mail), 319 Park
PI., Irvington, N. J.
RENOUF, E. Prince (M 1933), Mar., Air Cond.
Dept. (for mail), Straus Frank Co., and 1901
MacGrcgor, Houston, Texas.
RENTE, Harry W. (M 1931), IltR. Engr,, Oil
Burners, 70 W. Clnppcwa St., and (ior mail), 114
Morris Ave., Buffalo, N. Y.
RENTE, Sidney R. (A 1930), 31 Garrison Rd.,
WiWamsville, N. Y.
REI>KO, Joseph J, (S 1034), 4024 Ilamm Ave.,
Cleveland, Ohio.
RETTKW, Harvey F. (A/ 1929), Htg. anc^Vtfl.
JKngr., Board ot Education, 21st and Winter,
and (for mail), 6821 Martins Mill Rd,, Phila-
delphia, Pa,
REYNOLDS, Jack A. (J 1035; S 1933) Asst.
Engr., Sherman Mf#. Co., ana (for mail), 810
Fischer Av«., Sherman, Texas.
REYNOLDS, Thurlow W. (M 11)22), Consulting
Entjr., 100 Pinecrest Dr., Hawtings-on-IIudson,
N, Y.
REYNOLDS, Walter V. (A 1928), Pres., Walter
Reynolds, Inc., 8G1 Third Ave,, New York, N, Y.
RHEA, Chester A. (A 1031), Steel Boiler Renr.,
National Radiator Corp., 21M4 Arch St., and (for
mail), 722 Carpenter Lane, Philadelphia, Pa.
RICE, C. J. (A 1023), Pres. (for mail), Sterling
Kngrg, Co., 3738 N. Holton vSt., und 3370 N.
Summit Ave., Milwaukee, Wis.
RICE, Robert B. (M 1934), Aaaoc. Prof, in Mech.
Engrg. (for mail), Newark College of Engineering,
307 High St., Newark, and 105 Rutgers PL,
Nutley, N, J,
RICHARD, Edwin J, (M 1033), Owner (for mail).
Edwin J. Richard Equipment Co., Chamber of
Commerce Bldg,» and 3504 Paxton Ave., Cincin-
nati, Ohio.
RICHARDSON, Heitry G. (M 1034) » Vice-Press,,
Hawfey, Richardson, Williams Co., 204 Cooly
Bldg., and (for mail), 1433 Harvard Ave., Salt
Lake City, Utah.
RICHARDSON* Henry Thomas (A 1930), Vice-
Prea. (for mail), Richardson Sc Boynton Co,, 244
Madison Ave., and 156 East 79th St., New York,
N. Y.
RICHMOND, Jotm (S 1933), 5035 Forbes St.,
Pittsburgh, Pa,
RtCHTMANN, WilHam M.* (A 1932; J 1920).
Asst. Prof, of Bngrg, (for mail), Texas College of
Arts and Industries, and 709 W, Santa Gertrudes
St., Kingsvllle, Texm
RI00LE, Kemfole L, (.7 1985; S 1033), 4150
Windsor St, Pittsburgh, Pa,
RIBS, Lester S. (M 1929), Asst. Stipt. of Bldga,
and Grounds, University of Chicago, 060 East
5Sth St., and (for roaU)» $614 Bkckstone Ave.»
Chicago, III,
RIESMEYER, Edward H., Jr. (J 19301, Ht?.
Engr., Schaffer Htg. Co., 231-33 Water St., and
(for mail), 4702 Stanton Ave., Pittsburgh, Pa.
RIETZ, Elmer W.* (M 1923), Gen. Sales Mgr. (for
mail), Powers Regulator Co., 2720 Green view
Ave., Chicago, and 940 Greenwood Ave.,
Winnetka, 111.
RILEY, Champlain L. (M 1906), (Presidential
Member], (Pres., 1921; 1st Vice-Pres., 1920;
Council, 1918-1922), Clark, MacMullen & Riley,
Inc., 101 Park Ave., New York, N. Y.
RILEY, Edward C. (J 1935; S 1933), Research
Worker, Harvard School of Public Health, 55
Shattuck St., Boston, and (for mail), 51 Centre
St., Brookline, Mass.
RILEY, Robert G. (S 1934), 8S-37-179th St.,
Jamaica, N. Y.
RINEHARD, Wilson R. (J 1932), Choudrant,
La.
RITCHIE, A. Gordon (M 1933), Pres. and Mgr.
(for mail), John Ritchie, Ltd., 102 Adelaide St.
E., and 41 Garfield Ave., Toronto, Canada.
RITCHIE, Edmund J. (M 1923), yice-Pres.,
(for mail), Sarco Co., Inc., 183 Madison Ave.,
New York, and 2 Grace Court, Brooklyn, N. Y.
RITCHIE, William (M 1909), Vice-Pres., Boyn-
ton Furnace Co., 373 Fourth Ave., New York,
N. Y., and (for mail), 17 Van Reipen Ave.,
Jersey City, N. J.
RITTER, Arthur (M 1911), New York Dist. Mgr.
(for mail), American Blower Corp., 401 Broad-
way, New York, and 29 Edgemont Rd., Scars-
dale, N. Y.
ROBB, John M. (M 1913), Consulting Engr.,
1513 Columbia Terrace, Peoria, III.
ROBERTS, Henry L. (M 1916), Htg. Engr. and
Contractor (for mail), Henry L. Roberts, 228
North 16th St., Philadelphia, and 1014 AHston
Rd., Brookline, Delaware Co., Upper Darby
P. O., Pa.
ROBERTS, James R. (J 1934), Engr. (for mail),
Sutherland Air Cond. Corp., 627 Marquette
Ave., and 2423 Portland Ave. S., Minneapolis,
Minn.
ROBINSON, Harry C. (M 1930), Htg. Engr., 07U
Plcaaant St., Worcester, Mass.
ROCKWELL, Theodore F. (M 1933; A 1933;
J1932), Instructor in Htg. and Vtg. (for mail),
Carnegie Institute of Technology, and 131
Edgewood Ave., Edgewood, Pittsburgh, Pa.
RO0ENHEISKR, Georfte B. (M 1933), Head,
Htg. and Vtg. Dept. (for mail), David Ranken,
Junior School of Mech. Trades, 4431 Finney Ave.,
and 3639 A; Dover PL, St. Louis, Mo.
R.OIXSERS, Frederick A. (A 1934), Br. Mgr.,
Minneapolis-Honeywell Regulator Co., 4500
Euclid Ave., Cleveland, and (for mail), 2577
Ashton R,d.» Cleveland Heights, Ohio.
RODGERS, Joseph S. (/ 1034), Engr., Mont-
gomery Ward & Co., 1000 S. Monroe St., Balti-
more, and (for mail), 1 Third Ave., Brooklyn
Park, Md.
RODMAN, Robert W, (M 1922), Supt. of Plant
Operation (for mail), Board of Education, City
of New York, 500 Park Ave., and 175 West 73rd
St., New York, N, Y. *
ROEBUCK, William, Jr. (M 1D17), Mfrs. Repr.
(for mail), 311 Jackson Bldg., and 154 Sanders
Rd,, Buffalo, N. Y,
ROHX/IN, Karl W. (M 1930), Engr., Warren
Webster & Co., 17th and Federal Sts,, Caraden,
and (for mail), 4453 Terrace Ave., Merchant-
vffle,N. J*
RO3ULANI>, S. L. (A 1934), Design Engr., Okla-
homa Gas & Electric Co., Oklahoma City, Okla.
ROSE, Howard J. (M 1984), Sales Engr,, Fitz-
gibbons Boiler Co., Inc., 18& Main St., White
Plains, and (for mail), 100 Siebrecht PL, New
Rochelta, N. Y,
ROSEBERRY, John H. (U 1931), 32 Wardman
Rd., Kenmore, N, Y.
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
ROSEBROUGH, Robert M. (M 1920), Br. Mgr.
(for mail), L. J. Mueller Furnace Co., 4246
Forest Park Blvd., and 6012 McPherson Avc,,
St. Louis, Mo.
ROSELL, Axel F. (M 1035), Mgr. Gen Sales
Dept., Svenska Flaktfabriken Kungsgatan S,
Stockholm, and (for mail), Ku Atlas 0, Lidingo,
Sweden.
ROSENBERG, Philip (A 1928), Secy-Treas.,
Universal Fixture Corp., 137 West 23rd St., and
(for mail), 250 West 104th St., New York, N. V.
ROSS, John O.* (M 1920), Ross Industries Corp.,
350 Madison Ave., New York, N. Y.
ROSSITER, Paul A. (S 1935), SS Kent St.,
Minneapolis, Minn.
ROTH, Charles F. (A 1930), Mgr., International
Htg. and Vtg. Exposition, Grand Central
Palace, New York, and (for mail), 141 East 36th
St., New York (November 1 to April 30), and
Dreamthorp, Bedford Village, N. Y. (May 1 to
October 31).
ROTH, Harold Raymond (M 1935), Mgr.
Toronto Office (for mail), Canadian Sirocco Co.,
Ltd., Room 321, 57 Bloor St. W., and 18
Tichester Rd., Toronto, Ont, Canada.
ROTTMAYER, Samuel I. (.4 1933; J 1928),
Mech. Engr. (for mail), Samuel R. Lewis, 407
S. Dearborn St., and 1109 Hyde Park, Blvd.,
Chicago, 111.
ROWE, William A. (M 1921), (Council, 1920-
1931), 718 Longfellow Ave., Detroit, Mich.
ROWLEY, Frank B.* (U 1918), (Presidential
Member}, (Pres., 1932; 1st Vice-Pres., 1931; 2nd
Vice-Pres., 1930; Council, 1927-1933), Prof, of
Mech. Engrg. and Director of Experimental
Engrg. Lab., University of Minnesota, and (for
mail), 4801 E. Lake Harriet Blvd., Minneapolis,
Minn.
ROYER, Earl B. (M 1028), Designing Engr.,
Fosdick & Hilmer Consulting Engrs., 1703 Union
Trust Bldg., and (for mail), 603.5 Iris Ave.,
Cincinnati, Ohio.
ROZETT, William, Jr, (J 1935; S 1932), 3528 E.
Tremont Ave., New York, N. Y.
RUDIO, H. M. (M 1921), Mgr., Air Cond. Dept.
(for mail), Gustin Bacon Mfg. Co., 1412 West
12th St., and 0039 Kdgerale Rd., Kansas City,
Mo.
RUFF, DeWltt O. (M 1922), Heal y- Ruff Co,, 765
Hampden Ave., St. Paul. Minn.
RUGART, Karl (A 1924), Dist. Mgr. (for mail),
Warren Webster & Co., 20 South 20th St., and
5830 Willows Ave., Philadelphia, Pa.
RUPPERT, Edward H. (A 1923), 85 Eastern
1 Pkwy., Brooklyn, N, Y.
RUSSELL, Joseph Nelson (M 1890), Managing
Dir. (for mail), Rosaer & Russell, Ltd,, Romney
House, Marsham St., Westminster, and Per-
nacres Fulmer near Slough, Buckinghamshire,
England,
RUSSEIX, W. A. (M 1921), (Council, 1934), M«r.»
K. C. Br, (for mail), U. S, Radiator Corp., 1405
West llth St., and 230 Ward Pkwy., Kansas
City, Mo,
RUSSEIX, William B. (M 1928). Colorado Ave.,
R, F, D. No, 1., Jolict, 111.
RYAN, Marry J, (M 1022), 47 Harris Ave.,
Albany, N. Y.
RYAN, William F. '</ 1983), Sales Engr., Lee
Hardware Co,, 252*54 N. Santa Fe, and (for
mail), 600 E. Iron, Salina, Kans.
RY0ELL, Carl A. (M 1931; A 1031; J 1928) »
Owner, (for mail), C. A, Rydell Associates, 188
Dartmouth St., Boston, and 280 Qulnobequin
Rd,, Waban, Masa,
S
SABIN, Edward R, (M 1019). E, R, Sabin & Co.,
4710-12 Market St., Philadelphia, Fa,
SADLER, C. Boone (M 1028), Design Draftsman
(for mall), Public Works Office, llth Naval
District, and 4820 Voltaire St., San Diego, Calif,
SAITO, Shoseo (M 1923). Marunouchl Bldg,,
Opposite Tokyo Station, Tokyo, Japan,
SAKOUTA, Mathieu L. (M 1924), Consulting
Engr. and Expert Gavan, Simanskaia 4-A,
Leningrad, U. S. S. R,
SANBERN, E. Nutc* (Al 1023), 123 S. Haviland
Ave., Audubon, N. J.
SANDS, Clive C. (M 1929) G, P. O. Box 001 F. F.,
Sydney N. S. W., Australia.
SANFORD, Arthur L. (JU 1915), Mech. Engr.,
4240 Aldrich Ave. S., Minneapolis, Minn.
SANFORD, Sterling S. (<U 1930) , Engr. Sales (for
mail), Detroit Edison Co., 2000 Second Ave.,
and l.r)03 Soyburn Ave., Detroit, Mich.
SANTEE, Helen G. (At 1930), Asst. to Architect
and Engr., City School Dist., 81 N. Washington
St., and (for mail), 900 S. Kranklin St., Wilkes-
Barre, Pa.
SAUER, Robert L. (A IIWO), Dist. Sales Mgr. (for
mail), Rilcy Stoker Corp., Kt. of Walker St., and
3315 W. Philadelphia, Detroit, Midi.
SAUNDERS, Laurence F. (A! 19,'W), Director of
Engrg., Harrison Radiator Corp., Lockport,
N. Y.
SAWDON, Will M. (M 1920), Prof. Experimental
Engrg. (for mail), Cornell University, and 1018
E. State St., Ithaca, N. Y.
SAWHILL, R. V. (A 1929), _ Editor (for mail),
Domestic Engrg., 1900 Prairie Ave., Chicago,
and «r>34 Oakdalc Ave., Glencoe, 111.
SAWYER, J. Neal (J 1933), Production Dept.,
Jiolland Furnace Co., and (for mail), 78 East
12th St., Holland, Mich.
SCANLON, Edward S. (A 1934), 2510 Homehurst
Ave., Pittsburgh, Pa.
SCHEIOECKER, Dantol B. (A 1010), Secy, (for
mail), Hunter-Clark Vt«. Syatwn Co., 2800
Cottage Grove Ave,, ami 4020 N. Kilbourn Ave.,
Chicago, III.
SGHERNBBGK, Fred H. (A 1930), Salesman (for
mail), Win. Bros. Boiler & Mf«. Co., Nicollet
Island, and 5045 Portland Ave., Minneapolis,
Minn.
SGHIOK, Karl W. (A 1034), Salca Kngr., Minne-
apolis-Honeywell Regulator Co., 4500 Kuelid
Ave., and (for mail), 2044 Cornell Rd., Cleve-
land, Ohio.
SGHLICHTING, Walter G. {M 1932), Mgr., Air
Cond. Dept., Clara ge Kan Co., and (for mail),
1417 W. Lovell St., Kalamaxoo, Mich.
SCHMIDT, Richard H. <5 1934), 2130 Abinston
Rd., Cleveland, Ohio.
SGHMUTZ, Jfoan (M 1933), Head Mgr. (for mail),
P, R. S. M, 40 Rue Ameiot, Paris Xle, and 18
Rue DufrSnoy, Paris XVIe, France.
SCHNEIDER, WJlUam G. (Af 15*32), (for mail),
The American Bra$s Co., 25 Broadway, New
York, N. Y.
SCHO£tfUAHN, Robert P, (M 1910), Consulting
Engr. (for mail). «*{(H-5 Industrial Trust Bldg.,
and 710 Nottingham Rd., Wilmington, Del,
SGHQBNOFF, Alfred E. (/ 1935; $ ItKiQ), Secy-
Treas., Schoenoff Tlbg, & Htg. Co,, &U E»
Second St,, and (for mail), 513H E, Second St.,
Menornonie, Wi«.
SCHOEPFLIN* Paul H, (M 1920), Niagara
Blower Co., 0 East 45th St.» N«w York, N. Y.
SGHULZ, Howard I. (A 1915), Crane Co., 1228
W. Broad St., Richmond, V®.
SGHULZE, Benedict H. (M 1921). Eastern 6ntei
Mgr. (for mail), Kewanee Boiler Corp., 37 West
39th St., and 57 Purk Ave,, Ntw York, N. Y,
SGHUEMAN, Jfoba A, (J 1035), Air Cond. Enar,
(for mail), York Ic© Machinery Corp,, 2700
Washington Av«s. N,W», Clev^Itnd, and 1Q&9
Parktfde Dr,, L^kewood, Ohio,
SGBWARTC, Jacob (J 1020), Contmctor,
Samiiel Schwartz 8c Son, Inc., SO west 27th 8t»«
Bayonne. and (for mail), 12 van Hout&ia Ave»»
Jersey City, N. J»
SGHWEIM, Henry J. (M 1828), Chtef Saw* and
Secy, (for mail). Gypsum Am., 211 W, WIM "
Dr., and 1012 Estes Ave., Chicafo, r
SCOFIELP, Paul C, (J 19*
Carrier Easw. Corp,, 74S ]
and 800 N. <Ss ' ' " "^J
84
ROLL OF MEMBERSHIP
SCOTT, Charles E. (M 1907), Pres. and Treas.
(tor mail), Vapor Engrg. Co., 489 Fifth Ave.,
New York, N. Y., and Darien, Conn.
SCOTT, George M. (M 1915), Vice-Pres. (for
mail), Child & Scott, Donohue, Inc., 112 Wooster
St., New York, and GO Bowman Ave., Port
Chester, N. Y,
SCOTT, William P., Jr. (J 1933), 9 Scenic Way,
San Francisco, Calif.
SCR1BNER, Eugene D. (A 1933; J 1929), Engr,
(for mail), Carrier Engrg. Corp., Chrysler Bldg.,
R. 408 New York, N. Y., and 204 Prospect St.,
Westfield, N. T-
SEEBER, Rex R.* (M 1931), Head, Mech. Engrg.
Dcpt., Michigan College of Mining and Techno-
logy, Houghton, Mich.
SEELBACH, Herman (M 1931), Pres. (for mail),
Equipment Sales, Inc., 610 Erie County Bank
Bldu., Buffalo, and 31 Central Ave., Hamburg,
N. Y.
SEELEY, Lauren E.* (Al 1930), Asst. Prof, (for
mail), Yale Ensrj*. School, Yale University,
Mason Lab., and 130 Everit St., New Haven,
Conn.
SEELIG, Alfred E. (U 1920), Pres. and Gen.
Mgr,, L. J. Wing Mfg. Co., 154 West 14th St.,
and (for mail), 310 Convent Ave., New York,
N, Y.
SEELIG , Lester (M 1925), Mech. Engr., Museum
of Science and Industry, Jackson Park, and (for
mail), 725 Irving Park Blvd., Chicago, 111.
SEBPE, Paul E. (A 1933), Sales Engr., Minne-
apolis-Honeywell Regulator Co., 2831 Olive St.,
St. Louis, and (for mail), 8233 John PI., Wellston,
Mo.
SKITER, J. Earl* (M 1928), Asst. Mgr., New
Business Dept., Consolidated Gas, Electric
Light & Power Co., and (for mail), 7117 Bristol
Rd., Baltimore, Md.
SEKIDO, Kunisuke (M 1003), Consulting Engr.,
Marunouchi Bldg., No. 855, and (for mail), 10
Momo/Guo Nakano, Tokyo, Tanan.
SELLMA3N, Nils T. (M 1022), Director of Sales
and Utilisation, and Asst. Secy, (for mail),
Consolidated Gas Co. of New York, 4 Irving
PI., and f>(5 Wnlworth Ave., Seursdalc, N. Y.
SENIOR, Richard L. (M 1925), (for mail), R. I,,
Senior, Inc., 103 Park Ave., New York, and 10
Cherry Av«,» New Rochelle, N. Y.
SENNET, Lowell E, (S 1934), 1711) East 115th St.,
Cleveland, Ohio.
SBVERN8, William H.* (M 1033), Prof, of Mech,
Engr, (for mail), Dept, of Mech. Knzr&, Uni-
versity of Illinois, and 009 Indiana Ave., Urbana,
SBWAR0, Percival H,* (Charter Member; Life
Member), Research, 369 Washington Ave.,
Brooklyn, N. Y,
SHAKE, I, Ernest (A 1034), Sales Engr., B. F,
Sturtevant Co,, 80 Broad St., Boston, and (for
mail), 35 Keasenden St., Dorchester, Haas.
SHAN KLIN, Arthur P, (M 1021)), Sales Engr, (for
mail), Carrier B^ngrg. Corp., 12 South 12th St.,
Philadelphia, and 40 Amherst Ave., Swarthmore,
Pa,
SHANKXINt JoHn A. U4 1028), Secy-Treas, (for
mail). West Virginia Hfcg. & Plbg, Co,, 283 Hale
St., and 1507 Quarrier St., Charleston, W. Va.
SHARP, Floyd H. (M 1920-), H7 E, Third St.,
Jamestown, N. Y»
SHARP* Htmrv C, (M 1935), Mgr,, Oil Heat DIv,
-(for mafl), Smith Oil & Reining Co., HQ£
Kilburn Ave,, and 1928 Rockton Ave.r Rock-
ford. III.
SHAVER, Herbert H, (A 1*39). Asat. Gen. Sales
Agent (for mail), Hudton Coal Co., 424 Wyoming
Ave., and 1507 Wyoming Ave.t ScrtntGn, Pa,
SHAW, Burton E. (/ 1034), Research Chief,
Ollbtrt & Barker Mfo Co., Springfield, and (for
mail), Gnmby Rd,, Southwlck, Mass.
SHAW, Mftar (M 1920), Prea. (for mail), tynch
& Woodward, lac,, 820 Dow St., Bottom and
WT&oyal St, Woilaeton, Mass,
W, Harold W«a<m t$ 1905),
«M &t Paul,
SHAW, Norman J. H. (M 1927; J 1925), 37
Benjamin Rd., Arlington, Mass.
SHAWUN, Walter C. (A 1931), 696 S. Oak Park
Court, Milwaukee, Wis.
SHEA, Michael B. (M 1921), Sales Dept. (for
mail), American Radiator Co., 1344 Broadway,
Detroit, and 114 Massachusetts Ave., Highland
Park, Mich.
SHEARS, Matthew W. (U 1922), 39 Sylvan
Ave., Toronto, Ont., Canada.
SHEFFLER, Morris (M 1921), Pres, (for mail),
Sheffler-Gross Co., 203 Drexel Bldg., and 5451
Lebanon Ave., Philadelphia, Pa.
SHELDON, Nelson E. (M 1927), Dist. Sales Mgr.
(for mail), Carrier Engrg. Corp., 916 Temple
Bldg., and 41 Lanark Crescent, Rochester, N. Y.
SHELDON, William D., Jr. (J 1934), Chief
Engr., Sheldons, Ltd., and (for mail), Cedar St.,
Gait, Ont., Canada.
SHELNEY, Thomas (M 1931), Pres. (for mail),
Pierce Blower Corp., 27 Carolina St., and Hotel
Fillmore, Buffalo, N. Y.
SHENK, Donald Hugh (M 19341, 10G Forest
Lane, and (for mail), Riggs Hall, Clemson
College, S, C.
SHEPARD, Edward C. (M 1932), Owner (for
mail), Shepard Engrg. Co., 370 Lexington Ave.,
and 978 Grant Ave,, New York, N. Y.
SHEPARD, John deB. (J 1929), Consolidated
Gas, Electric Light & Power Co., Room 406
Lexington Bldg., Baltimore, Md.
SHEPPARD, Frank A. (M 1918), Salesman (for
mail), Johnson Service Co., 411 East 10th St.,
and 27 East 70th St., Kansas City, Mo.
SHEPPARD, William G. F. (M 1922), Partner
(for mail), Shcppard & Abbott, 119 Harbord
St., and 1 Clarendon Ave., Toronto, Ont.,
Canada.
SHERET, Andrew (M 1929; A 1925), Pres. (for
mail), Andrew Sheret, Ltd., 1114 Blanshard St.,
and 1030 St. Charles St., Victoria, B. C., Canada.
SHERMAN, Ralph A. (M 1933), Fuel Engr. (for
mail), Buttolle Memorial Institute, 505 King
Ave., and 1893 Coventry Rd., Columbus, Ohio.
SHIVERS, Paul F. (M 1930), Chief Engr., Minne-
apolis-Honeywell Regulator Co., Wabash, Ind.
SHODRON, John G. (M 1921), Consulting Engr.
and Research, 419 E. Milwaukee Ave., Ft.
Atkinson, Wis.
SHGRB, Will A. (M 1909), Treas., The Field &
Shorb Co., 705 N. Pine St., and (for mail),
3 Lincoln PL, JDecatur, 111.
SHROCK, John H. (M 1924), Mgr. (for mail),
New York, Blower Co., Factory St., and 1524
Michigan Ave., La Porte, Ind.
SHULTZ, Earl© (A 1919), Vice-Prea. (for mail),
Illinois Maintenance Co,, 1136-72 W. Adams"St.,
and Edgewater Beach Apts., Chicago, 111.
SIEB& Claude T, (A 1927), Service Systems
Kngr. (for mail), western Electric Co,, Inc.,
195 Broadway, New York, N. Y., and Russell
Rd., Fanwood, N. J.
SIECEL, L«o (M 1928; A 1925), Mech, Engr.,
1016 Lancaster Ave., Brooklyn, N. Y*
SIGMUND, Ralph W. (M 1932), Dist, Mgr. (for
mail), B. F. Sturtevatit Co., 913 Provident Bank
Bldg., and S04 Oak St., Cincinnati, Ohio.
SIMKIN, Milton (J 1935; S 1938), 103 Brighton
Ave,, Perth Amboy, N. J.
SIMQNDS» Abe H. (A 1935; J 1929), Sales Engr.
(for mail), Carrier Engrg. Corp. of California, 74,8
E, Washington Blvd., and 440 Westminster Ave,, *
Loa Angeles, Calif.
SIMPSON, Donald C. (M 1932), Supt. of Re-
search, Industrial Mat. Biv, (for mail), Owena,
Illinois Glass Co., Newark, ana 878 JCelton Ave,,
Columbus, Ohio.
SIMPSON, William KU (M 1919), Vice-Pres. (for
mail), Hoffman Specialty Co., an4 0 Sands St.,
Watertmry. Conn.
SK,H>MORB? Jfohti G, (J 19SO), Air Cond. Engr.,
Carrier Engrg. Corp,, 408 Chrysler Bldg., New
York, and (lor mail), 5101*a9th Ave., tong
Island City, N< Y,
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
SKINNER, Henry W. (M 1920), Consulting Engr.
(for mail), Box 1334, and 4816 Dexter, Ft.
Worth, Texas.
SKXENARIK, Louis (J 1928), 305 East 72nd St.,
New York, N. Y.
SLAYTER, Games (M 1931), OS Walhalla Rd.,
and (for mail), 711 Southwood Ave., Columbus,
Ohio.
SLIGHT, Irvin (A 1925), Slight Bros., 741 York-
way PL, Jenkintown, Pa.
SMAK, Julius R. (A 1934), Supt. of Service
Depts., Crane Co., South Ave., and (for mail),
3135 Park Ave., Bridgeport, Conn.
SMALL, Bartlett R. (J 1932), Sales Engr, (for
mail), T. C. Heyward, 1408 Independence Bldg.,
and 326 West 10th St., Charlotte, N. C.
SMALL, John D.* (M 1910), Consulting Engr.
(for mail), 127 N, Dearborn St., Chicago, and
411 Maple Ave., Wilmette, 111.
SMALLMAN, Edwin W. (M 1920), Navy Dept.,
and (for mail), S3J Allison St. N.W., Washington,
D. C.
SMITH, Elmer G.* (M 1929), Asst. Prof, of
Physics, Agricultural and Mechanical College of
Texas, College Station, Texas.
SMITH, Card W. (M 1927), Salesman, Premier
Warm Air Heater Co,, Dowagiac, Mich., and (for
mail), 248 Roche St., Huntington, Ind.
SMITH, Jared A. (A 1933), Br. Mgr. jffor mail),
The Bryant Heater & Mfg. Co., 626 Broadway,
and 3817 Indian View Ave., Mariemont, Cin-
cinnati, Ohio.
SMITH, J. Darrell (M 1933), Mech. Engrg. Dept,
Philadelphia Si Reading Coal & Iron Co., and (for
mail), 317 North 19th St., Pottsville, Pa.
SMITH, Milton S. (M 1019), Trcas., Carrier
Engrg. Corp., 850 Frelinghuysen Ave., Newark,
and (for mail), 13 N. Terrace, Maplewood, N. J.
SMITH, Robert Hugh (7 1934; S 1933), Sales
Engr., Sears Roebuck & Co,, Dept. of Plbg.,
Htg. and Vtg., 135 S. Fifth St., and (for mail),
214 N. Fourth St., Room 410, Steubenville,
Ohio.
SMITH, Wilbur F. (M 1920), Consulting Engr.,
000 Schuylkill Ave., Philadelphia, and (for mail),
422 Bryn Mawr Ave., Cynwyd, Pa.
SMOOT, Thco Halley (M 1935), Chief Engr, (for
mail), Fluid Heat Div,, Anchor Post Fence Co.,
Eastern Ave. and Kane St., and 2512 Talbot Rd.,
Baltimore, Md.
SHYERS, Edward €. (A 1933), Sales Engr.,
Minneapolis-Honeywell Regulator Co., 1013
Penn Ave., Wilkinaburg, and (for mail), 148
Jamaica Ave., West View, Pittsburgh, Pa.
SNEED, Richard B. (S 1934)> (for mail), College
of Engineering, University of Oklahoma, Norman
and Brlstow, Okla,
SHELL, Ernest (M 1920) ,'39 14 LeMay Ave,,
Detroit, Mich.
SNIDER, Lewis A. (M 1927), Pres. (for mail),
L. A, Snirler Engrg. Service, Inc., 005 N. Michi-
gan Ave. /and 049 Buena Ave., Chicago, 111.
SNYDER, Allen, K. (J 1930), Air Cond, Engr.,
Richmond Air Equipment Co., Inc., 1804 W.
Broad St, and (for mail), 4309 Grove Ave.,
Richmond, Va.
SNYDER, Jay W. (M 1017), McColl-Snyder-
McLean, 2304 Pcnobscot Bldg,, Detroit, Mich,
SNYDER, Joseph S, (A 1025), Sales Repr.,
Detroit Lubricator Co., 374 Delaware Ave., and
(for mail), 9 Knowlton Ave,. Buffalo, N, Y.
SODEMANN, Paul W. (M 1«; J 1920), Sales
Engr., 2300 Delraar Blvd.* and (for mail), 4130
Parlln Ave,, St. Loute, Mo.
SODEMANN, William C. B. (M 1019), Pre», (for
mail), Sodenmnn Heat & Power Co,, 2308
Delmar Blvd., St. Louis, Mo,
SONNEBORN, Gharkss (M 1930), Vice-Pres. in
charge of Production, Shaw, Perkins Mfg. Co.,
West Pittsburgh, and (for mail), R. D. No. 3,
New Castle, Pa.
SONNEY, Kermit J, (S 1034), (for mail), 310
W, Symmea St., Norman, 0kla,« and L, B, lad,
WIlcox, Pa.
SOPER. H. A» (U 1910), Vice-Free., American
Foundry & Furnace Co,, Bloomlngton, HI,
SOULE, Lawrence C.* (M 1908), Secy, and Chief
Engr. (for mail), Aerofin Corp., 850 Freling-
huysen Ave., Newark, and Essex Fells, N. J.
SPAFFORD, Allen (A 1027), Wood Conversion
Co., Cloquet, Minn.
SPECKMAN, Charles H. (M 1918), Prof. Engr.,
375 Bourse Bldg., Philadelphia, Pa.
SPFXLER, Frank N.* (M 190S), Director, Dept.
of Metallurgy and Research (for mail). National
Tube Co., 1922 Frick Bldg., and C-ill Darlington
Rd., Pittsburgh, Pa.
SPENCE, Morton R. (J 1934), Asat. Purchasing
Agent, Rundle & Spence Mf£. Co., 445 N.
Fourth St., and (for mail), 709 E. Lexington
Blvd., Milwaukee, Wis.
SPENCER, Roland M. (J 1934), Sales Enpjr, (for
mail), Powers Regulator Co., 754 Hippodrome
Annex, Cleveland, and 1269 Bonnie View Ave.,
Lakewood, Ohio.
SPIELMAN, Gordon P. (A 1031; J 1923),
Harrison, Spielman Co., 480 Milwaukee Ave.,
Chicago, 111.
SPIELMANN, Harold J. (M 1933), Air Cond.
Engr., The Vilter Mfg. Co., and (for mail), 2549
N. Lake Dr., Milwaukee, Wis.
SPITZLEY, Ray L. (M 1920), 1200 W. Fort St.,
Detroit, Mich.
SPOFFORTH, Walter (M 1930), Chief of Mech.
Services, U. S. Penitentiary, McNeil Island, and
(for mail), 1850 W. Blvd., Day Island, Tacoma,
Wash.
SPROULL, Howard B. (M 1920), Div, Sales Mgr.
(for mail), American Blower Corp., 1005-H
American Bids-, and 3588 Ray mar Dr., Cin-
cinnati, Ohio.
SPURGEON, Joseph H. (M 1924), Salesman (for
mail), Spurgeon Co., 5-203 General Motors
Bld#., and 17215 Pcnnington Dr., Detroit, Mich.
STAGEY, Alfred E., Jr.* (M 1914), Wooton Rd,,
Essex Fells, N, J.
STACK, Frank Charles (J 1035; S 1933), 140-23
Cherry Ave., Flushing N. Y.
STACY, Stanley C. (M 1931), Mech* Engr. (for
mail), Board of Education, 13 S, FiUhugh St.,
and 91 Cobfos Hill Dr., Rochester, N. Y.
STALB, Joseph O. (A 1934), New York Mgr.,
Parco Furnace Div,, Reading Iron Co., 143
Liberty St., and (for mail), 22 Partridge Ave.,
Ridley Park, Pa.
STAMMER, Edward L. (M 1919), Supt., Htg.
and Vtg., Board of Education Bldg., and (for
mail), 4430 Tennesee Ave., St. Louis, Mo.
ST ANGER, Ralph B. (M X920), Owner (for mail),
Robinson & Stanger, Empire IJldg,, Pittsburgh,
and Deer Creek, Church Rd., Glenshaw, Pa,
STANOLAND, &. F, (Charter Member), (2nd
Vice-Pres,, 1908; Bourd of Governors, 1005,
1906, 1909; Board of Mgrs.» 1895-1899; Council,
1800- 18»7), Kendall, N. Y.
STANNARD, James M.* (Life Mm&flv M 1906),
Prea-Treas, (for mnil), StannartI Power Equip-
ment Co., £3 W, Jackson Klvd,, Chicago, and
1403 KHnor PI., Kvanston, fit,
STAPLES, William II. (A 1924), Htg, and Vt«.
(for mail), Maguire Staples tfe Mason, 24 West
20th St., and £48 West 1 64th St., New York,
N. Y.
STARK, W, Elliott* (M 1020), (Council, 1932-
1934.), Research Engr,, Bryant Iteiter & Mfg,
Co,, 17825 vSt. Glair Ave,. Cleveland, and
(for mail)* 1875 Rosemontt Rc3U East Cleveland,
Ohio,
STEELS, John B. (M 1932), Chief Engr. (for
mail). Engrg. Dept,* Winnipeg School Board,
Ellen and William Avev, and 184 Waterloo St,
Winnipeg, Man,, Canada,
STEELEf Maurice G. (M 102% Product Engr.
(for mail). Revere Copper & Br&ts,, Inc»» Re-
search Dept,, and 006 N. Mudlson St*, Rome,
N. Y.
STEEN, Joseph M* (M 1929), Iron City Kt& Co,,
843 Jaeksonia St., Pittsburgh, Pa.
STEFFNER, Edward F. (J 1934), 1Q&17 Fortuae
cU Ohio,
36
ROLL OF MEMBERSHIP
STEGGALL, Howard B. (A 1934), Br. Mgr. (for
mail), U. S. Radiator Corp., 941 Behan St., and
1166 Murray Hill Ave., Pittsburgh, Pa.
STEINHORST, Theodore F. (M 1919), Treas.
and Gen. Mgr., Emil Steinhorst & Sons, Inc.,
612 South St., and (for mail), 1664 Brinckerhoff
Ave., Utica, N. Y.
STEINKELLNER, Edward J. (S 1935), 315-19th
Ave. S.E., Minneapolis, Minn.
STEINMETZ, C. W. Arthur (M 1934), Mgr. (for
mail), American Blower Corp., 402 Broad St.,
Newark, and 50 Oakwood Ave., Bogota, N. J.
STEPHENSON, L. A. (M 1917), Mgr. (for mail),
Powers Regulator Co., 409 East 13th St., and
801 West 57th Terrace, Kansas City, Mo.
STERNBERG, Edwin (A 1932; J 1931), Air
Cond. Engr., Arctic Engrg. Co., 123 White St.,
and (for mail), 58 East 92nd St., New York, N. Y.
STERNE, Cecil M. (A 1934), Chief Engr. (for
mail), Metropolitan Refining Co., Inc., 23-28
50th Ave,, Long Island City, and 115 Harold
Rd., Woodmere, L. L, N. Y.
STETSON, Lawrence R. (M 1913), 303 Congress
St., Boston, Mass.
STEVENS, Harry L, (M 1934; A 1927; J 1924),
Secy-Treas. (for mail), M. M. Stevens Co., 108
W. Sherman, and 7 West 22nd St., Hutchinson,
Kans.
STEVENS, John M. (A 1933), 4643 Morris St.,
Philadelphia, Pa.
STEVENS, William R. (A 1934), Partner, L. B.
Stevens Co., 442 E. Front St., Cincinnati, Ohio,
and (for mail), 159 Tremont Ave., Ft. Thomas,
Ky.
STEVENSON, Wilbur W. (M 1928), Steam Htg.
Engr* (for mail), Allegheny County Steam Htg.
Co*, 435 Sixth Ave., and 1125 Lancaster Ave.,
Pittsburgh, Pa,
STEWART, Charles W. (M 1919; A 1918),
Asst. Secy, (for mail), Hoffman Specialty Co.,
and 21 Yates Ave., Watcrbury, Conn.
STEWART, Clement W. (M 1934), Sales Engr,
(for mail), Ilg Electric Vtg, Co., 15 Park Row.,
and 3985 Saxon Ave., New York, N. Y.
STEWART, Duncan J. (A 1930), Mgr., Electric
Apparatus Div. (for mail), Barber-Colman Co.,
and 214 Franklin PI,, Rockford, 111.
STEWART, John C. (A 1934), Owner (for mail),
1844 Smith St., and 2807 Victoria Ave., Regina
Saek, Canada.
STILL* Fred R,* (M 1004), (Presidential Member),
(Prea,, 1918; 2nd Vicc-Pres., 1017; Council,
1916-1919), Vice-Pres, (for mail), American
Blower Corp., 401 Broadway, and 1 East End
Ave., New York, N. Y.
STILLER, Frederick Wilbur (J 1933), Estimator
(for mail), F. C. Stiller & Co., 121) S. Tenth St.,
and 138 West 49th St., Minneapolis, Minn.
STINARD, Rutherford L. (J 1934), Engr.,
American Radiator CoM 40 West 40th St., New
York, N. Y,. and (for mail), 1377 Boulevard B,
West New York, N, J.
STITT, Arthur B, (J 1085; S 1933), Plbg, and
Htg, Bngr,» Sears Roebuck & Co., 184 Atlantic
St., Stamford, Conn., and (for mail), 260 Valen-
tine Lane* Yonkers, N, Y.
STKTT, Eugenia W* (M 1917), Sales Repr., Cast
Product® Div. (for maii), 46 Second Ave»,
Johnstown, Pa,
STOCK.WBLL, William R. (M 1903; J 1901),
Weil-McLain Co,, Michigan City, IndU
STONE, Euftene R. (M 1913), 78 Woodbine St.,
y, Mass.
STONE, Georlfc F, (Life Member; M 1918),
Estimator, 19 Blmwood Rd.» Verona, N. J.
STRAUCH, Paul C. (A 1984), Sales Engn, The
Henry Furnace & Foundry Co., 18th and
Merriman Sta,, Pittsburgh* and (for mall), 101
Washington Ave,, Edgewood, Pittsburgh, Pa,
STRBVBLL, Rofter P. (M 19340, Co-Partner (for
mall), Wra* R, Hogg Co., 900 Fourth Ave,»
Asbury Park, and corner State Highway and
Victor R, Neptune, N, J.
STRICKLAND, Albert W. (A 1929), Htg. and
Vtg. Engr., Big Timber, Mont.
STROCK, Clifford (A 1929), Associate Editor (for
mail), Heating and Ventilating, 148 Lafayette
St., and 150 East 182nd St., New York, N Y.
STROUSE, Sherman W. (A 1934), Sales Engr.,
Cooney Refrigeration Co., Inc., and (for mail)
315 Capen Blvd., Buffalo, N. Y.
STROUSE, Sidney B. (M 1921), Engr. (for mail)
500-529 Guarantee Trust Bldg., and 22 S.
Illinois Ave., Atlantic City, N. J.
STRUNIN, Jay (J 1933), Engr. and Contractor
(for mail), Strunin Plbg. & Htg. Co., 408 Second
Ave., and 54 West 89th St., New York, N. Y.
STUBBS, W. C. (M 1934), Design Draftsman,
Heat and Vtg. (for mail), Norfolk Navy Yard,
and 36 Chanmng Ave., Portsmouth, Va.
SUMMERS, Ernest T. (A 1930), Pres. (for mail),
Summers, Darling & Co., 121 Smith St., and Ste.
22 Newcastle Apts., Winnipeg, Man., Canada.
SUNDELL, Samuel S. (J 1935; 5 1933), 3040
Longfellow Ave. S., Minneapolis, Minn.
SUPPLE, Graeme B. (M 1934), American Blower
Corp., 025 Architects and Builders Bldg.,
Indianapolis, Ind.
SUTCLIFFE, Arthur G. (M 1922; A 1918), Chief
Engr., Ilg Electric Vtg. Co., 2850 N. Crawford
Ave., and (for mail), 4146 N. St. Louis Ave.,
Chicago, 111.
SUTHERLAND, David L. (A 1934), Pres-Treas.
(for mail), Sutherland Air Cond. Corp., 627
Marquette Ave., and 1815 Colfax Ave. S.,
Minneapolis, Minn.
SUTTON, Frank (M 1932), Consulting Engr. (for
mail), 140 Cedar St., New York, and Babylon,
L. L, N. Y.
SWANEY, Carroll R. (M 1929; / 1921), Gilbert
Howe Gleason, 25 Huntington Ave., Boston,
Mass.
SWANSON, Harry (M 1933), Engr. (for mail),
The Fels Co., 42 Union St., Portland, and Box
135, Cape Cottage, Maine.
SWANSON, Rolf G. (S 1935), 324 Walnut St.
S.E., Minneapolis, Minn.
SWANSTROM, Alfred E. (J 1935; S 1932),
Construction Foreman, U. S. Dept, of Interior,
and (for mail), 1444 Van Buren St., St. Paul,
Minn.
SWEATT, Charles H. (S 1935), 4259 Unity Ave.,
Robbinsdale, Minn.
SWEIVEN, C. E, (S 1935), 406 Walnut St. S.E.,
Minneapolis, Minn.
SWENSON, John E» (A 1930), Industrial Engr.
(for mail), Minneapolis Gas Light Co., 800
Hennepin Ave., and 1102 South East 13th Ave.,
Minneapolis, Minn.
SWISHER, Stephen G., Jr, (A 1934), Sales Engr.
(for mail), The Trane Co., 125 E. Wells St., and
4238 N. Woodburn Ave., Milwaukee, Wis.
SYSKA, Adolph G. (M 1933), Consulting Engr.,
Syska & Hennessy, 420 Lexington Ave., New
York, N. Y,
SZEKEtY, Emeat (M 1920), Vice-Prea. and Gen,
Mgr. (for mail), Bayley Blower Co., 1817 South
60th St., and 3104 WJKilbourn Ave., Milwaukee,
Wis.
S2OMBATHY, Louis R. (A 1930), Ferguson
Sheet Metal Works, Inc., 34 N, Florissant Blvd.,
Ferguson, Mo.
TABOR, Charles B* (S 1935), 1815 University
Ave, S.E., Minneapolis, Minn,
TAGGART, Ralph C,* (M 19*12), 14 Lyon Ave.,
Menands, Albany, N. Y.
TAUAFERRO, Robert R.* (M 1919), Air Cond,
Engr,, Philadelphia Saving Fund Society, 12
South 12th St, Philadelphia, and (for mail),
$38 Beechwood Rd., Upper Darby, Pa.
TALLMADGE, Webster (M 1924), Prea. (for
mail), Webster Tallmadge & Co,, Inc., 255 North
18th St,, East Orange, and 7 Clareraont PL,
Montclair, N. J,
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
TARR, .Harold M. (M 1931), Htg. Engr., 21
Montague St., Arlington Heights, Mass.
TAUSON, Peter O, (S 1934), 408 Southwest 23rd
St., Oklahoma City, Okla.
TAVANLAR, Eligio J.* (J 1931), (for mail),
Carrier Research Corp., 850 Frelinghuysen Ave.,
Newark, N. J., and Binalonan Pangasinan,
Philippine Islands.
TAVERNA, Frederick F. (M 1928; A 1927;
J 1924), Engr,, Raisler Htg. Co,, 129 Amsterdam
Ave., New York, N. Y., and (for mail), 40G-12th
St., Union City, N". J.
TAYLOR, Edward M. (A 1934), Draughtsman
and Engrg. Asst., City Engineer's Dept., and (for
mail), 102 Innes Rd., Christchurch, New Zealand.
TAYLOR, William E. (A 1934), Factory Sales
Engr., Air Cond. Div. of (for mail), Gar Wood
Industries, Inc., 7924 Riopelle St., and 200S W.
Grand Blvd., Detroit, Mich.
TAZE, Donovan L. (M 1031), Sales En«r.,
American Blower Corp., 601)0 Russell St.,
Detroit, Mich.
TEASDALE, Lawrence A. (M 1920), Partner (for
mail), Oftice of Hollis French, 20 Ashmun St.,
and 262 West Rock Ave., New Haven, Conn.
TEELING, George A. (M 1930), Consulting
Engr., UN. Pearl St., Albany, N. Y.
TEMPLE, Walter J. (M 11TO, Engr,, J. A.
Temple & Co., 919 E. Michigan Ave., and (for
mail), 1215 Reed St., Kalamazoo. Mich.
TEMPLIN, Charles L. (M 1921), Sales Engr. (for
mail), Carrier Engrg. Corp., Bona Allen Bldg.,
and 781 Sherwood Rd. N.K., Atlanta, Ga.
TENKONOHY, Rudolph J. (A/ 1923), Vice-Pres.
(for mail), Airtherm Mfg. Co., 1474 S. Vande-
venter Ave., St. Louis, Mo,, and 5019 Ridgewood
Ave, Detroit, Mich.
TENNANT, Raymond J. J. (.4 1929), Supervisor
of Sales (for mail), Duqucsne Light Co., -135
Sixth Ave,, and 529 Navato PL, Pittsburgh, Pa.
TENNEY, Dwight (M 1032), Pres. and Chief
Engr. (for mail), Tenney Engrg., Inc., Bloomfield,
Ave., at Grove St., Bloomtiekl, and 33 Summit
Rd., Verona, N. J.
THEORELL, Hugo G. T.* (Life Member; M
1902), Consulting Engr., Hugo Theorells In-
genieussbyra, Skoldungagatan 4, Stockholm,
Sweden.
THINN, Christian A.* (M 1921), Chief Engr.,
C. A. Dunham Co., 450 K. Ohio St., Chicago, 111.
THOMAS, L. G. Lee (M 1934), Vice-Pres, (for
mail), Economy Pumping Machinery Co., 3431
Weat 48th PI., Chicago, and 426 Forest Ave.,
Oak Park, III.
THOMAS, Melvern F, (M 1900), Consulting
Engr, (for mail), Thomas & Ward ell, W) College
St., and 24 Rivercrest Rd., Toronto, Gnt,
Canada,
THOMAS, Norman A. (M 19^8), Pres. (fur mail),
Thomas Htg, Co., llth and Herrick Ave., and
824 Monroe Ave., Racine, Wis.
THOMAS, Richard H. (Life Member, M 192Q),
Economy Pumping Machinery Co,, 3431 West
48th PI., Chicago, 111.
THQMMEN, Adolph A, (A 1929), Forman,
Bloomer Htg, & Vtg, Co,r 1245 West 47th St.,
and (for mail), 3400 West Olst PI., Chicago, 111,
THOMPSON, Donald (J' 1088), Engrg, Dept,,
Carbide & Carbon Chemicals Corp., and (for
mail), 514 Simma St., Charleston, W, Va.
THOMPSON, Nelson S.* (M 1917; J 1807), 1615
Hobart St. N.W., Washington, D. C,
THOMSON. Thomas N.* (M1899) Consulting
Engr,, 87 Irwin PL, Huntinjfton, L, L, N, Y*
THORNBVRG, Harold A» (M 1932; A 1982;
J 1920), Sales Engr. (for mail). Carrier Enarg.
Corp,, U South 12th St., and 2115 Chestnut St.,
Philadelphia, Pa,
THORNTON, Roger T. (M 1910), Buffalo Forge
Co., 490 Broadway, Buffalo, N. Y.
THORNTON. William B.* (M 1931), Sales Bngr.
(for iaall}( Carrier Ensrg* Corp,, 404 Bona Allen
Bldg., Atlanta, a»d 155 Coventry Rdn l>eatur,
Ga.
THRUSH, Homer A. (If 1918), H. A. Thrush &
Co., 21-23 E. Riverside Dr., Peru, Ind.
TIBBETS, John G. (M 1920), Engrg. Dept.,
B. & O. R. R. Co., and (for mail), P.O. Box 106,
Ellicott City, Mel
TILLER, Louin (J 1935; 5 1933), 1724 Northwest
20th St., Oklahoma City, Okla.
TILTZ, Bernard E. (M 1930), Pres. (for mail),
Tiltz Air Cond. Corp., 285 Madison Ave., New
York, and 24 Barnum Rd., Larchmont, N, Y.
TIMMIS, Pierce (Af 1920), Service Equip. Dept.
(for mail), United Engineers & Constructors,
Inc., 1401 Arch St., Philadelphia, and 202 Mid-
land Ave., Wayne, Pa,
TIMMIS, W. Walter (M 1933; A 1025), Engr. (for
mail), American Radiator Co., 40 West 40th St.,
New York, and 32 Oak Lane, Glen Cove., N. Y.
TISNOWER, William (JU 1923), 131 Livingston
St., Brooklyn, N. Y.
TITUS, Marvin S. (M 1028), 414 Fayctte St
Charleston, W. Va.
TJERSLAND, Alf (M 1910; J 1900), K. Sunde &
Co., Ltd., Oslo, Norway.
TOBIN, George J. (M 190o), Owner, vSanitary,
Htg. & Vtg. Engr., 1S7 North Ave., Plainiield,
N. J.
TOBIN, John F, (A 1934), Salesman, American
Blower Corp., Rra. 1404, 228 N. LaSalle St.
Chicago, 111.
TOONDER, Clarence L. (HI 1933), Air Cond.
Engr,, Sales Engrg, Dept., Kelvinator Corp.,
Plymouth Rd., and (for mail), 12701 Strattnoor
Ave., Detroit, Mich.
TORNQUIST, Earl L. (A 1934), Supervisor,
Distribution Operation (for mail), Public Service
Co. of North Illinois, 72 W, Adams St., Chicago,
and 465 Parkside Ave., Klmhurst, 111,
TORR, Thomas W. (M 1933), Chief Engr., The
Rudy Furnace Co., P. O. Box 73, Dowagiac,
Mich.
TORRANCE, Henry (M 1933), Pres., 17,">
Christopher St., and (for mail), 11:4 East 17th
St., New York, N. Y.
TOUTON, R. IX (M 1033), Tech, Director (for
mail), Bayuk Cigars, Inc., Ninth and Columbia
Ave,, Philadelphia, and 19 Lodges Lane, Cymvyd,
Pa.
TOWER, Elwood S. (A/ 1930), Engr,, 1114
Koppers Bldg., and (for mail), 1411 WJghtman
at., Pittsburgh, Pa.
TRANE, Reuben N.* (A* 1915), Prea, (for mail),
The Trane Co., and 126 South 15th St., LaCrosse,
Wis.
TRAUGOTT, Mortimer (A 1030), East Sales
Mgr. (for mall), Bryant Heater & Mftf. Co., 152
North 15th St., Philadelphia, and 721 Meeting
House Rd., Klfcina Park, Pa.
TREADWAY, QiHmtita (J 1082), Sales Engr. (for
mail), Chrage Fan Co., 707 Security Bank Bldg.,
ami 2018 ColHngwood, Toledo, Ohio,
TRIMMER, Charles M. (J 1035: S 1033),
Inspection and Testing, Rockland Light 8s
Power Co,, 105 Pike St., and (for mall), 28
Prospect St., Port Jervfs, N* Y,
TROS&K, Joseph J. (A mi), Vlefc-Pres, and
Oru Mgr, (for mail), Vand«*Troske Co., 236
Winter Ave, N.W., and 233 Brown St. S.E.,
Grand Rapids, Mich.
TRUITT, Joseph E. (M W30; A mi), Pret,»
Autovent Fan &, Blower Co., 1805 N* ICostner
Ave., Chicago, III,
TRULS0N, Arthur F. (M 1830), Mech, Engr,,
1509 W. Sixth Si,, Ashland, Wla*
TRUMBOt SUas M. (A 1926), Sales (for mil),
Buffalo Forge Co.. 20 N, Wacker Dr., Chicago,
and 0^1 Fmnfclia St., Bowttftn Orove^ III,
TRUMP, Charles G. (M 1934), Pm and M. B*
(for mail), Jam«a Spear Stove & Htg, Co.. l§33
Market St., Philacfelphia, and 608 Baird M*t
Marion, Pa. »
TUCELER, Franfc N. (M l&20}t FbUd Ba^r,. Bf
Electric Vtg, Co., Room UOi 18 Parte Row,
Nw York, and (for mat!)* ft» Wlml^r $t.
Freepott, L. L, N, Y.
ROLL OF MEMBERSHIP
TUCKERMAN, George E. (M 1932), Mgr,
Philadelphia Br., Air Cond. Div. (for mail),
York Ice Machinery Corp., 1238 North 44th St.,
and 6202 Ogontz Ave., Philadelphia, Pa.
TURLAND, Charles H. (M 1934; .4 1930), Mgr.,
Htg. 4 and Vtg. Dept., Kipp- Kelly, Ltd., 68
Higgins Ave., and (for mail), 325 Centennial St.,
Winnipeg, Man., Canada.
TURNAU, Edmund H. (J 1935; S 1933), Cadet
Engr., Koppers Seaboard By-Product Coke Co.,
and (for mail), 23 Polifly Rd., Hackensack, N. J,
TURNER, George G. (A 1934), Western Repr.
(for mail), Heating and Ventilating, 228 N.
LaSalle St., Chicago, and 803 Elmwood Ave.,
Evanston, 111.
TURNER, John (M 1930), Sales Engr. (for mail),
Minneapolis-Honeywell Regulator Co., 285
Columbus Ave., Boston, Mass., and Contoocook,
N. H.
TURNER, John W. (M 1928), Chief Engr. (for
mail), Pacific Steel Boiler Div., Box 1488,
Detroit, and 26031 Concord Rd., Royal Oak,
Mich.
TURNER, Mebane E. (M 1934), Mech. Engr.,
R. J. Reynolds Tobacco Co., and (for mail),
643 Holly Ave., Winston Salem, N. C.
TURNO, Walter G. W. (M 1917; A 1912), Secy.,
H. W. Porter & Co., Newark, and (for mail),
71 Lafayette Ave., East Orange, N. J.
TUSGH, Walter (M 1917), Htg. and Vtg. Engr.,
Tcnney & Ohmes, Inc., 101 Park Ave., New
York, and (for mail), 881 Sterling PL, Brooklyn,
N.Y,
TUTTLB, George H.* (J 1934), Htg. Engr. (for
mail), The Detroit Edison Co., 2000 Second Ave.,
and 982Q Belle Terre, Detroit, Mich.
TUTTLE, J. Frank (M 1913), Sales Agent (for
mail), Warren Webster Co., Kewanee Boiler
Corp., 127 Federal St., Boston, and 2 Elmwood
Ave., Winchester, Mass.
TUVE, George L.* (M 1932), Asso, Prof, of Mech.
Engrg, (for mail), Case School of Applied Science,
and 1294 Cleveland Heights Blvd., Cleveland,
Ohio.
TWIST, Charles F. (M 1921), Secy, (for mail),
Ashwell-Twist Co., 907 Thomas St., and 2310
Tenth Ave. N., Seattle, Wash.
TYLER, Roy 0, (M 1928), East Salea Mgr, (for
mail), Modine Mfg. Co., 101 Park Ave., New
York, and 15 Highbrook Ave., Pclham, N, Y.
TYSON, William H. (M 1928), Mgr, of Engrg.
(for mail), Goodyear Tyre & Rubber Co., Ltd.,
and "Kipewa" Codsall Rcl, N.R., Wolver-
hampton, England.
U
UHL, Edwin J. (M 1025), Uhl Co., 132 S, Tenth
St., Minneapolis, Minn.
UHL, WiHiard F. (M 1018), (for mail), Uhl Co.,
132 S, Tenth St., and 4716 Lyndale Ave, S.,
Minneapolis, Minn.
XJHLHORN, W, J. (M 1920), 733 S, Highland
Ave., Oak Park, III
ULLMAN, Herbert G.* (A 1928), Mgr, Mech,
Product Development Lab, .American Radiator
Co,, P, 0. Box 850, Second St., Beechwood Ave,,
New Rqchelle. and (for mail), 107 White Rd.,
Sctrsdale, N. Y.
0RDAHL, Thomas H. (M 1980), Consulting
Engr, (tor mall). 726 Jackson PI, RW,t and
150&-44th St. N.W., Washington, D, C.
VALE, Henry A. L* (M 1929), Managing Director
(for mall), Vale Co,, Ltd,, 141-43 Amasffo St.,
Chriatehureh, and 241 Ham Rd., Fftttdalton,
Chrietchurcb,, New Zealand.
VAN ALBN, Walter T. (AC 1024), Htg, and Sale*
Ingr. (for mail), 1610 Seventh Are,, and 1800
Darlington Rd,, Beaver Falls, Pa.
VAN ALSBURG, Jerold H. (M 1931), Engr.,
Hart & Cooley Mfg. Co., and (for mail), R. No. 3,
Holland, Mich.
VANCE, Louis G. (M 1919), Partner (for mail),
Vance-McCrea Sales Co., West 27th and Sisson
Sts., and 3800 Egerton Rd., Baltimore, Md.
VANDERHOOF, Austin L. (A 1933), (for mail),
A. L. Vanderhoof, Inc., 2341 Carnegie Ave.,
Cleveland, and 3120 Yorkshire Rd., Cleveland
Heights, Ohio.
VAN HORN, Howard T. (A 1933), Dist. Mgr.,
Detroit Stoker Co., 1217 McKnight Bldg., and
(for mail), 4537 Grand Ave., Minneapolis, Minn,
VERMERE, Earl J. (M 1929), Sales Engr.,
Kewanee Boiler Corp., Warren Webster & Co.,
2341 Carnegie Ave., Cleveland, and (for mail),
2125 Wyandotte Ave., Lakewood, Ohio.
VERNIER, Marcel G. (J 1935; S 1933), 730 Hill
Ave., Willdnsburg, Pa.
VERNON, J. Rexford (M 1928; A 1926), (for
mail), Johnson Service Co., 1355 Washington
Blvd., Chicago, and 1020 Austin St., Evanston,
111.
VETLESEN, G. Unger (M 1930), 3 East 84th St.,
New York, N. Y.
VINCENT, Paul J. (M 1931), Paul J. Vincent Co.,
2133 Maryland Ave., and (for mail), 3807 Beech
Ave., Baltimore, Md.
VINSON, Neal L. (J 1935; 5 1932), 630 Clyde St.,
Pittsburgh, Pa., and (for mail), Box 3007, Lowell,
Ariz.
VIVARTTAS, E. Arnold (M 1910), Consulting
Engr., 121 Parkside Ave., Brooklyn, N. Y.
VOGEL, Andrew (M 1926), Engr. (for mail),
General Electric Co., and 1821 Lenox Rd.,
Schenectady, N. Y.
VOGELBACH, Oscar (U 1923), 23 William St.,
North Arlington, N, J.
VOGT, John H. (A 1925), Mech. Engr. (for mail),
New York State Dept of Labor, 80 Centre St.,
New York, and 87 Grant Ave., Brooklyn, N. Y,
VOGT, Joseph B. (M 1933; A 1933; J 1929),
1304 Grayton Rd., Grosse Point Park, Mich.
VOISINET, Walter E. (M 1930), Sales Repr. (for
mail), Buckeye Blower Co,, 250 Delaware Ave.,
Buffalo, and 151 Warren Ave., Kenmore, N. Y.
VOLK, Joseph H. (M 1923), Pres. and Treas. (for
mail), Thos. E. Hoye Htg. Co., 1906 W, St. Paul
Ave., and 2965 South 43rd St., Milwaukee, Wis,
VROOME, Albert E. (M 1932), Engr., E. I,
duPont deNemours & Co., duPont Bldg.,
Wilmington, Del., and (for mail), 412 Morton
Ave., Rutledge, Pa.
W
WACHS, Louis J. (/ 1930), Engr., Carrier Engrg.
Corp., Chrysler Bldg., New York, and (for mail),
354 East 21st St., Brooklyn, N. Y.
WAECHTER, Herman P. (A 1930; J 1927), Air
Cond. Engr., York Ice Machinery Corp., Brook-
lyn, and (for mail), 89 Sherman Ave., Tompkin&-
vllle, N. Y.
WAGNER, A. M. (A 1921), Mgr. (for mail),
American Radiator Co., 1741 W. St. Paul Ave.,
and 1857 N. Prospect Ave., Milwaukee, Wia.
WAGNER, Frederick H., Jr. (M 1934), Mgr. Air
Cond. Dept., New York Office (for mail),
American Blower Corp., 401 Broadway, New
York, and 1126 Post Rd., Scaradale, 'N. Y.
WAITB, Harry (A 1929), 1409 North 17th St.,
Superior, Wia.
WAL0ON, Charles D. (A 1632), Consulting
Ena;r,, Spencer Foundry Co*, Penetang, Ont.,
and (for mail), 82 Femdale Ave., Toronto,
Ont,, Canada.
WALSCER, Alexander (A 1025), Br. Mgr, (for
mail), C. A, Dunham Co., Ltd., 1807 Fifth SL
W.f and 0Q3~13th Ave. W., Calgary, Alberta,
Canada.
WALKER, Edmund R. (M 1934), Salea Mgr.,
Htg. Div* (for mail), Feddera Mfg. Co., Inc» 57
Tonawanda St., and 696 Crescent Ave., Buffalo,
N. Y.
39
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
WALKER, J. Herbert* (M 1916), Supt. of
Central Htg. (for mail), The Detroit Edison Co.,
2000 Second Ave., Detroit, and 432 Arlington Rd.,
Birmingham, Mich.
WALKER, William Kirby (M 1935), Develop-
ment Engr., American Radiator Co., 40 West
40th St., New York, N. Y.
WALLACE, George J. (M 1923), Principal
96-19-35th Ave., Corona, and (for mail), 27-36
Ericsson St., East Elmhurst, N. Y.
WALLACE, James Bee (A 1935), Dist. Repr.,
Taco Heaters, Inc., New York, N. Y., and (for
mail), 16921 Sorrento Ave., Detroit, Mich.
WALLACE, Kenneth S. (M 1931), Htg. Engr.,
Peoples Gas Light & Coke Co., 1520 Milwaukee
Ave., and (for mail), 5737 Kenmore Ave.,
Chicago, 111.
WALLACE, William M, II (M 1929), Air Cond.
and Htg. Contractor, 192 Lexington Ave., New
York, and (for mail), S908-19Gth St., Hollis,
L. I., N. Y.
WALLICH, A, C. (M 1919), Wallich Ice Machine
Co., 517 E. Larncd St., and (for mail), 1GG7
Burlingame Ave., Detroit, Mich.
WALSH, James A. (A 1932; J 1929), Pres. and
Mgr. (for mail), James A. Walsh, Inc., Architects
Bldg., Philadelphia, and Gwynedd Valley, Pa.
WALSH, J. Lee (A 1934), Sales Mgr. and Engi.,
May Oil Burner Corp., Maryland and Oliver
Ave., and (for mail), Temple Ct. Apts., 34th and
Guilford Ave., Baltimore, Md.
WALTERS, Arthur L. (M 1920; ,4 1925; J 1924),
7284 Richmond PI., Maplewood, Mo.
WALTERS, William T. (M 1917), Engr., Illinois
Engrg. Co., Corner 21st St. and Racine Ave., and
(for mail), 7905 Phillips Ave., Chicago, 111.
WALTHER, Vernon H. (M 1928; J 1925), Mech.
Engr,, 6821 Osceola Ave., Edison Park, Chicago,
111.
WALTERTHUM, John J. (A 1922) , Htg. Con-
tractor, 173 East 62nd St., New York, N. Y., and
(for mail), 42-A Van Reipen Ave., Jersey City,
N. J.
WALTON, Charles W., Jr. (M 1934), Mech.
Engr. (for mail), Rockefeller Center, Inc., 30
Rockefeller Plaza, New York, N. Y,, and 120
Monte Vista Ave., Ridgewood, N. J.
WANDLESS, Franklin W. (M 1925), Registered
Engr. (for mail), 1518 Fairmount Ave., Phila-
delphia, and Berwyn, Pa.
WARD, Frank James (M 1935), The Frank J.
Ward Co., Cold Spring, Ky.
WARD, Oscar G. (M 1919), Dist. Repr. (for mail),
Johnson Service Co., 1230 California vSt., and
1607 Jasmine St., Denver, Colo,
WARING, J. M. S, (M 1932), Consulting Kn«r.
(for mail), Chase & Waring, 17 East 42nd St.,
and 277 Park Ave,, New York, N. Y.
WARREN, Clarence N. (M 1919), Vice-Prea,,
Hayes Bros., Inc., 236 W. Vermont St., and (for
mail), 419 East 48th St., Indianapolis, Ind,
WARREN, Francis C, (M 1934), Salesman (for
mail), American Blower Corp., 228 N. LaSalle
St., Chicago, and 127 East Ave., Park Ridge, 111.
WARREN, Harry L. (M 1930), 130S Huntington
Pr,, South Pasadena, Calif.
WASHBURN, Marcus J. (A 1934), Insulation
Engr, (for mail). Eagle- Picher Lead Cq., Temple
Bar Bldg,, and 2211 Park Ave.» Cincinnati, Ohio,
WASHINGTON, G<M>r&e (M 1934), Sales
"for mail), Hoffman Specialty Co,, 130 N. Wells
St., Chicago, and 4327 Johnson Ave., Western
Springs, 111,
WASHINGTON, Laurence W. (M 1929), 2301
Knox Ave., Chicago, 111,
WATERMAN, Joh» H. (M 1031), Engr, (for
mail), Chas. T. Main, Inc., 201 Devonshire St.,
Boston, and 7 Centre St., Cambridge, Masa,
WATERS, Georfte G. (M 19S1; A 11)20), Dist.
Mgr. (for mall), American Blower Corp., I4tf8
Oliver Bldg,, and 52 Vernon Dr., Pittsburgh (l«),
Pa.
WATSON, M. Barry (&/ 1028), Consulting Engr.,
121 Welland Ave., Toronto 5, Canada.
WAXJNG, Tsing F. (J 1933), Htg. Engr., Ander-
sen, Meyer & Co., Ltd., and (for mail), No. 16,
Lane 152, Edinburgh Rd., Shanghai, China.
WEBB, John S. (M 1920), 16 Brookline St.,
Needham, Mass.
WEBB, John W. (M 1926), Managing Dir., Webb
Dust Removing & Drying Co., Ltd., Princess St.
Works, and (for mail), G Meadows Rd., Heaton
Chapel, Stockport, England.
WEBSTER, E. Kcssler (M 191,5), Warren Webster
& Co., 17th and Federal Sts., Camden, N. J.
WEBSTER, Warren (Life Member; M 1906;
A 1S99), Warren Webster & Co., 17th and
Federal Sts., Camden, N. J.
WEBSTER, Warren, Jr. (M 1932; A 1932;
J 1927), Vice-Pres-Treas. (for mail), Warren
Webster & Co., 17th and Federal Sts., Camden,
and Washington Ave. and Colonial Ridge,
Haddonfield, N. J.
WECHSBERG, Otto (M 1932), Pres. and Gen.
Mgr., Coppus Engrg. Corp., 344 Park Ave., and
(for mail), 1006 Main St., Worcester, Mass.
WEGMANN, Albert (A/ 1918), 0200 North 17th
St., Philadelphia, Pa.
WEIL, Martin (A 1925), Vice-Pres. (for mail),
Weil-McLain Co., 641 W. Lake St., and 4259
Hazel Ave., Chicago, 111.
WEIL, Maurice I. (A 1928), Pres. (for mail),
Chicago Pump Co., 2330 Wolfram St., and 1409
Elmdale Ave., Chicago, 111.
WEIMER, Fred G. (A 1919), Salesman, Kewanee
Boiler Corp., 1741 W. St. Paul Ave., and (for
mail), 3958 N. Stowcll Ave., Milwaukee, Wis.
WEINSHANK, Theodore* (Life Member; A/
1906), (Board of Governors, 1913), 3307 Holden
Ave., Chicago, 111.
WEISS, Arthur P, (A/ 192S), 134 Farrington
Avt\, North Tarry town, N. Y.
WEISS, Carl A. (A 1924), Supt. (for mail),
Kornbrodt ICornicft Ko., 1811 Troost Ave., and
29 East 68th St., Kansas City, Mo.
WEITZEL* Paul H. (S 1934), Cameron B.
Weitzel, and (for mail), 122 E. High St., Man-
heim, Pa.
WELCH, Louis A., Jr. (A 1929), 443 Second St.,
vSchcncctady, N. Y.
WELDY, Lloyd 0. (M 1930), Sales Kngr. (for
mail), Powers Regulator Co., 2720 Greenview
Ave., and 2846 North 77th Av«.» Chicago, 111,
WELSH, Harry S. (A/ 1906) , Sales Engr., Weil-
McLuin Co., and (for mail), 53 Kemphurst Rd.,
Rochester* N. Y.
WELTER, M. A. (A 1925) (for mail), Twin City
Furnace Co., 410-12 W. Lake St., and 4«06 £,
Garfield, Minneapolis, Minn,
WENDT, Ed&ar F» (M 1918), Prea. (for mail),
Buffalo Forge Co., 400 Broadway, ancl 120
Lincoln Pkwy., Buffalo, N, Y,
WEST, Perry* (M 1911), (Council, 19»(M92fi:
Treas., 1924-1925), Consulting Engr. (for mail),
13 Central Ave., and 445 Ridge St., Newark, N. J,
WETZELL, Horace E, (M 1934), Chief Engr, (for
mail), The Smith & Oby Co., 0107 Carnegie
Ave., and 8790 KIsraere Dr., Cleveland, Ohio*
WHAIXON, Fletcher (S 1935), 3852 Lyndale
Ave. S., Minneapolis* Minn.
WHEELEK, Otto J. (M 1923), Prea-Trets, (for
mall), The Samuel A. Essweln Htg, & Plbg. Co..
548-558 W. Broad St., and 3044 Collingswood
Rd.t Columbus, Ohio.
WHELLER, Harry S. (M 1016), Vice-Pres., L, J.
Wing Mfg. Co*, 154 West 14th St., New York,
and (for mail), 725 Union Ave., Elizabeth, N, J,
WHITE, Eu&wfc B» (M 1934), Architect and
Engr. (for mall], Y, M, C, A,» 19 S, USalte St.,
Chicago, and 300 N, Taylor Ave., Oak Park, III
WHITE, Everett A. (M 1021), Engrg. Dept.,
Crane Co., 30 South 10th St., and (for mail),
5244 Nottingham St., St. Louis* Mo.
WHITE, El wood S. (M 1921) t Pres. (for mm*I),
Taco Heaters. Inc., Room 1224, U% Madiaon
Ave., New York. N, Y., and M«adowbank Rd,,
Old Greenwich, Conn.
40
ROLL OB MEMBERSHIP
WHITE, John C. (M 1932), State Power Plant
Engr. (for mail), (324 E. Main St., and 622 E.
Main St. Madison, Wis.
WHITELAW, H. Leigh (M 191G), Vice-Pres. (for
mail), American Gas Products Corp., 40 West
40th St., New York, N. V., and Overbrook Lane,
Daricn, Conn.
WHITELEY, Stockett M. (M 1933), Consulting
Engr. (.for mail), Baltimore Life Bldg., and 3931
Canterbury Rd., Baltimore, Md.
WIIITMER, Robert P. (M 1935), Secy., American
Foundry & Furnace Co., and (for mail), 1402 E.
Washington St., Bloomington, 111.
WH1TSON, Lee S. (S 1935), 48*1 Harriet Ave.,
Minneapolis, Minn.
WHITTALL, Ernest T. (A 1933), Vice-Pres. (for
mail), May Oil Burner of Canada, Ltd., 196
Adelaide St. W., and 11 Cottingham Rd.,
Toronto, Ont., Canada.
WIEGNER, Henry B. (M 1919), Mgr., Boston
Office, Johnson Service Co., 20 Winchester St.,
Boston, and (for mail), 143 Standish Rd., Water-
town, Mass.
WIERENGA, Peter O. (A 1931), Vice-Pres. (for
mail), C. C. James Co., 49 Coldbrook St. N.E.,
and 231 Brown St. S.E., Grand Rapids, Mich.
WIGGINS, Oswald James (J 1935; 5 1933),
Walnut Grove, Minn.
WIGGS, G. Lome (A 1932; J 1924), Consulting
Engr. (for mail), University Tower, and 4,797
Grosvenor Ave., Montreal, Que., Canada.
WIGLE, Bruce M. (A 1920), Pres. (for mail),
Bruce Wigle Plbg, & Htg. Co., 9117 Hamilton
Ave., and 18114 Oak Dr., Detroit, Mich.
WILDER, Edward L. (M 1915), Mgr., Gas Sales
(for mail), Utility Management Corp., 120 Wall
St. New York, and 149 Mt. Joy Place, New
Roche-lie, N. Y.
WILEY, Edgar 0. (M 1909), Wiley & Wilson,
Lyiichburg, Va.
WILIIELM, Joseph E. (S 1934), 1355 West 87th,
Cleveland, Ohio.
WILKINSON, Farley J. (M 1933), Engr.,
Montgomery Ward & Co., Chicago, and (for
mail), 18257 Martin Ave., Homewood, III.
WILLARD, Arthur Cutts* (M 1914), (Presi-
dential Member}, (Pres., 1928; lat Vice-Pres,,
1927; 2nd Vice-Prcs., 1926; Council, 1925-1929),
Prea. (for mail), University of Illinois, President s
Office, and 711 Florida Ave,, Urbana, 111.
WILLEY, Earl C. (M 1934), Mech. Kngrg.
Instructor, Oregon State College, and (for mail),
1052 "A" St., Curvallia, Ore,
WILLIAMS, Alien W, (A 1915), Managing Dir-
ector (for mail), National Warm Air Htg, & Air
Conditioning Assn., 50 W. Broad St., Columbus,
and f>l Meadow Park Ave., Boxley, Ohio.
WILLIAMS* Frank H. U 1934), Air Cond.
Tester, Frigiclaire Div., General Motors, Prigi-
daire Corp., and (for mail), 14 Grand Apts,,
n, Ohio,
WILLIAMS* J. McFarland, Jr. (A 1928; J 1927),
Sales Kngr,» 1407-3fith St. N.WM Washington,
D. C,
' WILLIAMS, J. Walter (M 1916), Prea. (for mail),
Forest City Plbg, Co., 382-80 E. State St., and
928 E. State St., Ithaca, N. Y,
WILLIAMS, Leo E. (A 1933; J 1930), Viscose
Co,, and (for mail), 827 Liberty St., Meadville,
Pa,
WILLIS, Leonard L. (3 1935), 1212 Oliver N.,
Minneapolis, Minn.
WILMOT, Charles S, (M 1919). (for mail), 106
South 16th St,» Philadelphia, ana 406 Essex Ave.»
Narberth, H,
WXLSON, Georfi© T. (M 1925). Sales Engr,,
Gumey Foundry Co.. Ltd., 4 Junction Rd.,
Toronto, and (for mail), Tyre Ave., Islington,
Qnt., Canada,
WILSON, Harold AM Jr. (J 1933), General Sales
Dept, American Radiator Co., 40 W«st 40th St,
and (for mall), 113B Park Am» New York, N, Y.
WILSON, Raymond W, (M 1934), Member of
Firm (for mail), Wilson-Brinker Co., 412 Pythian
Bldg., and 429 Creston Ave., Kalamazoo, Mich.
WILSON, W. H. (A 1932), Steamfitter Foreman,
Pullman Car & Mfg. Corp., 11001 Cottage
Grove Ave., and (for mail), 22 West 110th PL,
Chicago, 111.
WILSON, William H. (A 1923), Br. Mgr. (for
mail), Johnson Service Co., 507 E. Michigan St.,
and 2023 E. Olive St., Milwaukee, Wis.
WINANS, Glen IX (M 1929), Engr. of Steam
Distribution (for mail), The Detroit Edison Co.,
2000 Second Ave., and 161S3 Wisconsin, Detroit,
Mich.
WINQUIST, Walter J. (A 1930), Htg. and Vtg.
Engr., 294 Nostrand Ave., Brooklyn, N. Y.
WINSLOW, G.-E. A.* (M 1932), Prof, of Public
Health (for mail), Yale University, 310 Cedar
St., and 314 Prospect St., New Haven Conn.
WINTERBOTTOM, Ralph F. (M 1923), Htg.
Engr., Winterbottom Supply Co., Commercial
and Miles, and (for mail), 1002 Riehl St., Water-
loo, Iowa.
WINTERER, Frank C. (M 1920), Sales Mgr. (for
mail), Cochran Sargent Co., Broadway and
Kellogg Blvd., and 830 Juno St., St. Paul, Minn.
WINTHER, Anker (J 1932), Air Cond. Engr.,
York Ice Machinery Corp., 2110 Gilbert Ave.,
Cincinnati, Ohio.
WISE, Daniel E. (S 1934), 10805 Lee Ave.,
Cleveland, Ohio.
WITHER, Charles N. (J 1930), Dist. Dealer
Supv. (for mail), Carrier Engrg. Corp., 2022
Bryan St., and 4154>£ Prescott St., Dallas,
Texas.
WOESE, Carl F, (M 1934), Consulting Engr. (for
mail), Robson &; Woese, Inc., 1001 Burnet Ave.,
and 256 Robineau Rd., Syracuse, N. Y,
WOHL, Maurice W. (M 1934), Engr., American
Insulating Corp., 377 Atlantic Ave., and (for
mail), 32 Lenox Rd., Brooklyn, N. Y.
WOLF, J. C. (M 1923), Drafting Room Engr. (for
mail), B. F. Sturtevant Co., and 44 Central Ave.,
Hyde Park, Mass.
WOOD, Frederick G. (J 1931), Sales Air Cond.
Kngr. (for mail), Westerlin & Campbell Co.
(Agents York Ice Machinery Corp.), 1113
Cornelia Ave., and 1905 Estes Ave*, Chicago, 111.
WOOD, J. Sydney (M 1926), Estimator (for
mail), Bennett & Wright, Ltd., 72 Queen St. E.,
and 163 Briar Hill Ave., Toronto, Ont., Canada.
WOODMAN, L. E, (M 1934), Pres. (for mail),
Woodman Appliance & Engrg. Corp., 203 E.
Capitol, and 1014 Fairmount, Jefferson City,
Mo.
WOODRUFF, Wilbur 3, (M 1933), Woodrutf
Coal Co,, 206 N. Broadway. Urbana, 111.
WOODS, Edward H. (M 1934), Prop, (for mail),
F. H. Higgins, 311 E. State St., and Hook PL,
Ithaca, N. Y.
WOOLLARD, Mason S. (M 1934), Draftsman.
H. H. Angus Consulting Engr., 1221 Bay St., and
(for mail), 31 Hillcrcat Park Ave,, Toronto, Ont.,
Canada,
WOOLSTON, A, H. (M 1919), 2015 Sansom St.,
Philadelphia, Pa.
WORSHAM, Herman (M 192d; J 1018), Frial-
daire Sales Corp., Dayton, Ohio, and (for man),
103 N, Walnut St., East Orange, N. J,
WRIGHT, Clarence E. (J 1935; 5 1033), Part-
time Instructor in Htg., Carnegie Institute of
Technology, Carnegie Tech., and (for mail), 270
N, Bellefield Ave*, Pittsburgh, Pa.
WRIGHT, Kenneth A. (M 1921), Johnson
Service Co,( 1113 Race St., Cincinnati, Ohio.,
and 113 Orchard St., Ft. Mitchell, Ky. ,
WRIGHT, M, Bfcrney (A 1982; J 1929), Astt.
Prof, of Mech. Enjfrg. (for mail), The Drexel
Institute, Philadelphia, and 228 Essex Ave.,
Narberth, Pa,
WUNDERLICH, Milton $»* (M 1925), I&iulit*
Co., Minneapolis, and (for mail), 1^8 Laurel
Ave,, St. Paul, Minn,
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
WYLIE, Howard M. (M 1925; J 1917), Vice-
Pres. in charge of Sales (for mail), Nash Engrg.
Co., and 51 Elrnwood Ave,, South Norwalk,
WYMORE, Fred C. (J 1935; S 1933), 100 West-
port Rd., Kansas City, Mo.
YAGER, John J. (M 1921), 425 Woodbridge
Ave., Buffalo, N. Y.
YAGLOU, Constantin P.* (M 1923), Asst.
Prof, of Industrial Hygiene (for mail), Harvard
School of Public Health, 55 Shattuck St., Boston,
and 10 Vernon Rd., Belmont, Mass.
YARDLEY, Ralph W. (U 1920), Asst. Archt.,
Board of Education, City of Chicago, 228 N.
LaSalle St., Room 568, Chicago, 111., and (for
mail), c/o Judge J. W. Galbraith, Farmers Bank
Bldg., vSuite 601, Mansfield, Ohio.
YATES, Geor&e L. (S 1934), Oklahoma University,
Albert Pike Hall, Norman, and (for mail), 1220
Johnstone, Bartlesville, Okla.
YATES, James E. (M 1934), Mgr. (for mail),
Yates, Neal&Co., 231 Tenth St., and 431-16th
St., Biandon, Manitoba, Canada.
YATES, Walter (Life Member; M 1902), Govern-
ing Dir. (for mail), Matthews & Yates, Ltd.,
Cyclone Works, and Parksend Swinton, Man.,
England.
ZACK, Hans J. (M 1928), Zack Co., 2311 Van
Buren St., Chicago, 111.
ZIBOLD, Carl Edward (M 1929), Mech. Engr.,
Htg. and Vtg. Co., Colonial Terrace, West-
minster Ridge, White Plains, N. Y.
ZIESSE, Karl L. (A 1931), Secy-Treas. (for mail).
Phoenix Sprinkler & Htg. Co., 115 Campau
Ave. N.W., and 315 Hampton Ave. S.E., Grand
Rapids, Mich.
ZIMMERMAN, Alexander H. (A 1930), Venti-
lation Engr., Chicago Board of Health, 707
City Hall, and (for mail), 5147 N. St. Louis
Ave,, Chicago, 111.
ZINK, David D. (M 1931), Consulting Engr. (for
mail), Zink Home and Bldg. Service, 225 Pkwa
Theatre Bldg., Kansas City, and Hickman's
Mill, Mo.
ZOKELT, C. G. (M 1921), ConsultiriK Engr.,
381Q-24th Ave. S., Seattle, Wash.
ZUHLKE, William R. (M 1928), 530 McLean
Ave., Yonkcrs, N. Y.
Summary of Membership
(Corrected to January 1, 1935)
UNITED STATES
Alabama 1
Arizona 3
Arkansas 3
California 34
Colorado „ 5
Connecticut 30
Delaware 5
District of Columbia 16
Florida 3
Georgia 6
Illinois. 195
Indiana 18
Iowa 6
Kansas 2
Kentucky.... 6
Louisiana 3
Maine - 4
Maryland 21
Massachusetts 103
Michigan . 94
Minnesota 117
Missouri 81
Montana 3
Nebraska... 2
New Jersey 100
New York 357
North Carolina 7
North Dakota 1
Ohio 101
Oklahoma 27
Oregon 1
Pennsylvania 210
Rhode Island 5
South Carolina 2
Tennessee 6
Texas 21
Utah 1
Vermont 3
Virginia 12
Washington 24
West Virginia 5
Wisconsin , 50
1694
FOREIGN COUNTRIES
Australia 3
Belgium.... 1
Canada..... „ 89
China
Czechoslovakia „ fw, 1
Denmark. , *»..,.....„„. 1
England . 16
France..
Germany.
Holland.
India......
Ireland
Italy
Japan *.,„ 5
Mexico. 3
New Zealand 3
9 Norway . 2
Phillipine Islands 1
Scotland , 1
South Africa ,..„.*. 1
Sweden » 3
n s. a PL,.-™... i
Total Membership. — ....
156
,1850
SUMMARY OF MEMBERSHIP BY GRADES
Honorary Members ...«„« .»,«. 2
Presidential Members ...... 23
Members,..,.... «,«»,.........«»....,....... .« « *. 1156
Associate Members... , 539
Junior Member**.... .,«. 233
Student Members*..,*,, , * 97
1850
LIST OF MEMBERS
Geographically Arranged
UNITED STATES
ALABAMA
San Francisco —
Stamford —
ILLINOIS
•n A T
Wnirf T W
Birmingham —
Cochran, L. H.
Corrao, J.
Torrington — Blooming ton —
Lichty, C. P.
Haley, H. S.
Doster, A. MaGirl, W. J.
Hudson, R. A.
soper, H. A.
ARIZONA
Krueger, J. I.
Waterbury — Whitmer, R. P,
Leland, W. E,
Scott, W. P., Jr.
Ahlberg, H. B. Qh
icago —
Tucson —
Moreau, D.
Phoenix-
South Pasadena —
Warren, H. L.
Hutzel, H.F. Acoeriy, j. j.
Simpson, W. K. Arenberg, M. K.
Stewart, C. W. Baurngardner, C. M
Black, F. C,
Keys, L. F.
COLORADO
Holte, E' E '
T
DELAWARE Borlinir. t7p
Lowell*-*-
Bracken, J. H,
Vinson, N. L.
Colorado Springs •*
•
t^aun. L. 1\
ARKANSAS
Davis, A. F.
Jardine, D. C.
Wilmington— Broom, H. A.
Fort Smith—
Herrick, L.
Pine Bluff—
Denver: —
McQuaid, D. J,
O'Rear, L. R.
Ward, 0. G.
Lownsberry, B. F, rhS'JJuH^ T'
Schoenijalm, R. P. $S?p"b.W< K
Cron<?. (1 Tt. TT-
Greer, W. R.
CONNECTICUT
DISTRICT OF <
Cunningham, T. M.
Siloam Springs —
COLUMBIA
Cutler, J, A.
Jones, C. R,
Bridgeport—
•-•'V.UU, i1 , J ft 1 I',
— - — - DeLand, C. W.
CALIFORNIA
Faile, K, H,
Smak, J. R,
¥,y , , Doherty, R.
Washington— Dunham, C, A,
Beitzell, A. E. 3
iramert, L. 1>,
Fairfield—
Brown, W» A,
Cric8«<m, K. B.
Berkeley —
Osborn, W, J.
Coward, H. Kvleth, K. B.
Duncan, G, W., Ji.
Beverly Hills-
Greenwich —
Jones, A. L.
Downea, H. II. Finan, J, J,
Febrey, E. J. KiUaeruld, M. J.
Feltwell, R. H. Fleming, J, P.
Nelson, H. A.
Oppcrman, E. F.
Frankel, G. S. Foster, T. R,
Huntin&ton Park—
Manchester—
Gardner, S, F. Frank, J, M,
Hood, 0. P. Gardner, W.. Jr>
Barman, W, E,, Jr.
Buck, L,
Kiczalea, M. 0, Gaylord, F, H.
Los Angeles—
Anderson, C.*S,
Millard, J. W,
New Britain—
Mayette, C. E, Getschow, G. M,
Ourusoff, L. S. Getschow, R. M,
Smallman, E. W. Gibbs, F, C,
Binford, W, M.
Bullock, H, H,
Hjerpe, C. A., Jr.
Thompson* N. S. Goelz, A, IL
Urdahl, T, H» Goaaetl. E. .1,
Cranston, W, E,, Jr.
EUingwood, E. L.
Hill, F. M,
Holliday, W. L,
Hungerford, L.
Kendall, E, H,
Kennedy, M.
New Haven—
Greenburg, L.
Hughes, C, K.
Seeley, L, E.
Teasdale, L, A.
Winslow, C.-E. A.
Williams, J. M,, Jr,
FLORIDA
Graves, W, B.
laag, S. L.
iainesi, J. J,
tiale, J. R
Flanley, T, F,t Jr.
Iwt.H, M,
Htattii, R, K,
,._„,, ,
Ft. Lauderdale—
Kooistra, J. F.
Ness, W, H. C.
Drear, A, G,
Ott, 0. W.
Park, J, F,
New London—
Chapin, C. G,
Forsberg, W,
Hopson, W. T.
Charlton, J, F* :
West Palm Beach—
Htayden, C. F,
g»mJ;J. B
Wayward. R, B,
Hteckd, E, P.
f-fjarUWs* t t
Pierce, E. D,
Norwaik—
pto!Tbw'L" HiTCEv:"
Polderman, JU H,
Scofield, P, C,
Mead, E, A,
Hlncldey, H. B,
Simonds, A. H,
Oakland—
Riverside--
Murphy, J. R»
Horton, 1C F,
— Howttt, J,
. . .. HowelL L.
Cummings, G, J,
Pasadena—
South Norwalfc—
Adams, H. E,
Atlanta— ]
Clare, F. W,
Kent, L, F,
Hiubbard, G, W.
rluttoel, A, U.
enninp, W, G.
Giftord, R, L,
Harvey, A* D.
Klein, E, W.
toion, L S.
San Diego
Sadler, C. B,
Jennings, L C.
Lyona, C, J,
Wylte, H, M,
McKinney, W, J,
T«mplln, C. L,
Thornton, W, B, !
'ohns, H. B,
'ohnton, C» W,
£***** A*» w T&
vcency, j? . t .
44
ROLL OF
MEMBERSHIP
Kehm, H. S.
Wood, F. C.
INDIANA
LOUISIANA
Kreiasl, H. G.
Zack, H. J.
Lagodzinski, H. J.
Lautenschlager, F,
Zimmerman, A. H.
Evansville —
Choudrant —
Lawler, M. M.
Cicero —
Bulleit. C. R.
Rinehart, W. R.
Lees, H. K.
Lewis, S. R.
Keppner, H. W,
Huntington —
New Orleans —
Lockhart, H. A.
Machen, J. T.
Decatur —
Smith, G. W.
Gammill, 0. E., Jr.
May, G. E.
Malone, D. G.
Shorb, W. A.
Indianapolis —
Malvin, R. C.
Marschall, P. J.
Martin, A. B.
Matchett, J. C.
Mathis, E.
Elmhurst—
Potvin, L. J.
Evanston —
Ammerman, C. R.
Fenstermaker, S. E.
Hagedon, C. H.
Hayes, J. G.
Kruse, R. W.
MAINE
Auburn —
Fowles, H. H.
Mathis, H.
Mathis, J. W.
Hayes, J. J.
Moore, R. E.
Ott, R. C.
Poehner, R. E.
Portland —
Mathis, V. J.
Shivers, P. F.
Pels, A. B.
Mauer, W. J.
Homewood —
Supple, G. B.
Merrill, C. J.
May, M. F.
McCauley, J. H.
Wilkinson, F. J.
Warren, C. N.
Swanson, H.
McClellan, J. E.
McDonnell, E. N.
McFarland, W. P.
Joliet —
Russell, W. B.
Lafayette —
Hoffman, J. D.
MARYLAND
Mcllvaine, J. H.
Mert/, W. A.
Kewanee —
LaPorte —
Baltimore —
Miller, F, A.
Bronson, C. E.
Shrock, J. H.
Axeman, J. E.
Miller, J. E.
Miller, R. T.
Milliken, J. H.
Dickson, R. B.
HaitmanXJMM.
Pursell, H. E.
Michigan City—
Stockwell.iW. R.
Collier, W, I.
Hall, M. S.
Lednum, J. M,
Mittendorff, E. M,
Mueller, H, C.
Murphy, E. T.
Narowetz, L. L., Jr.
LaGrange —
Eaton, B. K.
Peru—
Pyle, J. W.
Thrush, H. A.
Leilich, R. L.
Maccubbin, H. A.
McCormack, D.
Morris, E. J.
Needier, J. H,
Neiler, S, G.
Linn, H. R.
St. Mary-of-the-
Posey, J.
Seiter, J. E.
Nelson, C. L,
Moline—
Woods
Shepard, J, deB.
Newport, C. F.
O'Brien, J. H.
Beling, E. H.
Nelson, H. W.
Bisch, B. J.
Smoot, T. H.
Vance, L. G.
Often, B.
Nelson, R. H.
IOWA
Vincent, P. J,
Olscn, C. F.
Otis, G. K.
Walsh, J. L.
Peller, L.
Whiteley, S. M.
Pitcher, L. J .
Pope, S. A.
Powers, F. W.
Mt. Vernon—
Benoist, L. Lt
Ackley—
Nelson, G. O.
Brooklyn Park —
Rodgers, J. S.
Prentice, (), J.
Price, C, K.
Rusmuasen, R. P.
Norwood Park —
Olson, B.
Cedar Rapids-
Chandler, C. W.
Chevy Chase —
Dalla Valle, J. M,
Raymond, F. I.
Reger, H. P,
Reid, H. P.
Oak Park—
Blanding, G, H.
Council Bluffs —
Huffacker, H. B.
Ellicott City—
Tibbets, J. C.
Ries, L. S.
May, E, M.
LeMars —
Rockville
Rieu, E, W.
Rottmayer, S, L
Nightingale, G. F.
Uhlhorn, W. J.
Mathey, N. J.
Brunett, A, L,
Sawhill, R, V.
Scheideeker, D. B,
Schweim, H. J.
Peoria—
Farnsworth, J. G,
Sioux City—
Hagan, U. V.
Roland Park—
Dorsey, F. C.
Seelig, L,
Shultz, E.
Small, J. D.
Meyer, F. L,
Robb, J. M,
Waterloo—
Winterbottom, R. F.
MASSACHUSETTS
Snider* L. A.
Spielman, G, P.
Rocfcford—
KANSAS
Arlington —
Stannard, J. M,
Braatz, C, J.
Shaw, N. J. H,
Sutcliffe, A, G,
Thhm, C, A,
Dewey, R. P,
Merwin, G. E.
Hutchinson —
Arlington Heights—
Thomas, L, G, L.
Sharp, H. C,
Stevens, H. L,
Tarr, H. M.
Thomas, R. H,
Thommen, A. A.
Tobin, J, F.
Stewart, D» J.
Urbana —
Salina—
Ryan, W, F.
Boston-
Archer, D. M.
Tornqulst, E. L,
Truitt, J, E.
Brodericfc, E. L.
Fahnestock, M. K.
KENTUCKY
Bartlett, A. C,
Berchtold, E, W,
Trumbo, S. M.
Konzo, S.
Boyden, D. S.
Turner, G. G.
Vernon, J. R,
Wallace, K, S*
KraU, A. P.
Severna, W. H,
Willard, A. C.
Cold Spring— '
Ward, F. J.
Brinton, J. W.
Brissettet L. A,
Bryant, A, G.
Walters, W, T,
Walther, V. H.
Warren, F. C,
Woodruff, W, J,
Villa Park—
Ft, Thomas —
Stevens, W. R.
Bullock, T, A.
Cumminga, C. H.
Drinker, P.
Washington, G.
Washington, L, W.
Armapach, 0, W,
Lexington —
Dusossoit, E. A.
Edwards, D. J.
Well, M,
Weil, M, L
Weinihank, T.
Weidy, L. 0,
White, E. B,
Wllinette—
Norris, W. 0,
Wlanetka—
O'Bannon, L. S.
Louisville —
Helbtrom, J.
Murphy, H. C,
Foulds. P, A. L.
Franklin, R. S.
Gleason, G. H.
Hajek, W, J*
Herrick* D, A.
Wilson, W. H,
Ellis, B, B,
Reed, W, M.
Hilliard, C, E,
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Hoyt, C. W.
Melrose —
Detroit—
Holland—
Keefe, E. T.
Cole, E. Q,
Akers, G. W.
Cherven, V. W.
Kelley, J. J.
Dodge, H. G.
Arnoldy, W. F.
Sawyer, J. N.
Kellogg, A.
Gerrish, G. B.
Baldwin, W. H.
Van Alsburg, J. H.
Kimball, C. W.
Barth, H. E.
McCoy, T. F.
Milton—
Bishop, F. R.
Houfihton —
Merrill, F. A.
Miller, J, F. G.
Moulton, D.
Mitchell, C, H.
Needham —
Blackmore, F. H.
Boalea, W. G.
Booth, H. N.
Seeber, R. R.
Kalamazoo — •
Osborne, M. M.
Park, C. D.
Brennan, J. W,
Brinker, H. A.
Plunkett, J. H.
Rydell, C. A.
Webb, J. S.
Chappell, H. D.
Chester, T,
Downs, S. H.
McConner, C. R.
Shaw, E.
Newton Center —
Collamore, R.
Temple, W. T.
Stetson, L. R.
Swaney, C. R.
Murray, J. J.
Connell, R. F.
Coon, T. E.
Wilson, R. W,
Turner, J,
Tuttle, J. F.
Waterman, J. H.
Yaglou, C. P.
Newton ville —
Emerson, R. R.
McMurrer, L. J.
Cooper, F. D.
Cummins, G, H,
Darlington, A. P.
Dauch, E, O.
Adams, E. 1.
Distel, F.
McLouth, B. F.
Brookline —
Riley, E. C.
Quincy —
Gesnier, J.
Stone, E. R.
Dubry, E. E.
Egglcston, L. W.
Feely, F. J.
Giguerc, G. H.
Parsons, R. A.
Muskegoii Heights —
Reid, H. F.
Cambridge —
Baker, R. H,
Flint C T
Reading —
Ingalls, F, D. B.
Glanz, E.
Hamlin, H. A.
Hare, W. A.
St. Joseph —
Milliken, V. D.
Haddock, L T,
Revere —
Harms, W. T.
Holt, J. W.
Ivahan, C.
Foulds, S. T, N.
Harrtgan, E. M.
Heydon, C. G.
MINNESOTA
Lees, J. T.
MacDonald, E. A.
Cochltuate —
Ahearn, W. J.
South Hadley—
Colby, C. W.
South wick—-
Shaw, B. E.
Kilner,' J/S/
Kirkpatrick, A, H,
Knibb. A. E,
Luty, D. J.
Maler, G. M.
Cloquot —
SpafTord, A,
Duluth—
McColl, J, R.
Foster, C..
Dal ton —
Da kin, H. W.
Springfield-™
Brown, W. M.
McConachie, L. L.
McIntSre, j. F.
Minneapolis—
Aikcn J F
E. Dedham —
Higgins, T, J.
Cross, R. E.
Holmes, R, E.
Leland, W. B.
McLean, D.
Milward, R. K,
Morse, C. T,
Algrcn, A, B.
Anderson, XX B.
Dorchester-
Murphy, W. W.
O'Neil, J. M.
Olson, R. G.
Paetz, H. E.
Armstrong, R. W.
Brown, M.
Goodrich, C. F.
Hosterman, C. O.
Shaer, I, E.
Waban—
Jones, W. T.
Watertown —
Parrott, L. G,
Partlan, J. W,
Purcell, F. C.
Purcell, R. E.
Randall, W, C.
Bctta, H. M.
Bjerken, M, H.
Bredeaen, B, P.
Bull, A. S.
Fltchburg—
Wiegner, H. B.
Rowe, W. A.
Sanford, S, S,
BuotF A* V.
Burns, JtC. J.
Karlson, A. F.
McKittrick, P, A.
Wollesley Hills-
Barnes, W. E.
Sauer, R. L.
SchHchting, W. G.
Burritt, C. G.
Butts, R, L.
Harwich Port —
Gilling, W. F., Jr,
Shea, M, B.
Copperud, E, R.
Maxwell, G, W.
Holbrook—
Nason, G. L,
Hyde Park-
Ellis, F. R.
Epple, A, R.
Fritzberg, L, H,
Keyes, R. K,
Wolf, J, C,
Ipswich--*-
Monroe, R. R.
West Roxbury—-
Christie, A, Y,
McPherson, W, A.
Weymouth —
Clough, L.
Winchester—-
Jackson, A, B.
Woburn—
Parker, P.
Wollaaton—
Hodgdon, H. A,
Snyder/J. W,
Spifcsley, R, L.
Spurgeon. J. H.
Taylor, W, E.
Taze, 0, L.
Toonder, C. L,
Turner, J. W.
Tuttle, G. H.
Walker, J. H,
Wallace, J, B.
WalHch, A, C.
Wigle, B, M,
Winant, G. D,
DahMrom, G. A,
Dovolis, N, J,
Forfar, D, M,
Gelb, A.
Gcrrigh, H. E.
Gordon, E. B., Jr.
Gordon, W, J»» Jr.
Gross, L. C,
Haatvedt, S. R.
Hall, J, R.
Hanson, L, P,
Han-la, J. B,
Hildebrandt, H. A.
Hitchcock. P» C.
Howard, E.
Bride, W, T*
Worcester—
Robinson, H. C.
Firestone, J, F,
Torr, T. W.
Johnson, L, H.
Jonea, N, W.
JLeomtoter —
Wechaberg, 0.
E. Lart«I«t&—
Jordan, L» E»
Jordan, R. C.
Kern, R, T.
Miller, L» G,
KJtngt R, L,
MICHIGAN
Grand Rapid*-—
Bmdfteld, W, W,
Leigh, R. L,
Kntttdtaoru C. M»
Kuehn, W. C,
KuempeL L, L,
Ktins, Jt W.
Brigham, F. H.
Ann Atbor —
Lvntt-—
Backus, T, H, L,
Morton, C. H.
Fselmn, J, B,
Battle Creek—
Troske, J, J.
Wierenga, P, 0,
Leslie, !0, B»
Gates, W, A.
Christenson, H.
Ziesae, K. L.
Lewis, C. B,
Medford—
!
Grosso Point Park*""
Lowe, H, ».
Lundi C» K»
Citshman, L, D,
ftadjltfcy, J. N,
Vogt, J, B.
ROLL OF
MEMBERSHIP
Magney, G. R.
MISSOURI
Rosebrough, R. M.
Elizabeth-
Martenis, J. V.
Maynard, H. R.
Sodemann, P. W.
Sodemann, W. C. B.
Burke, J. J.
Cherne, R. E.
Miller, H. A.
Ferguson —
Stammer, E. L.
Cornwall, G. L
Miller, L. B.
Mjolsnes, L. 0.
Szombathy, L. R.
Tenkonohy, R. J.
White, E. A.
Grant, W. A.
Morgan, G. C.
Morton, H. S.
Myers, C. R.
Jefferson City —
Woodman, L. E.
Webster Groves —
Myers, G. W. F.
Merle, A.
Wheller, H. S.
Nelson, R. A.
Kansas City —
Ranck, G. L.
Essex Fells—
Noble, T. G.
Oatrin, A.
Pappenfus, W. G.
Pfeifer, O. J., Jr.
Porter, H, M.
Adams, C. W.
Allan, N. J.
Arthur, J. M.
Betz, H. D.
Wellston—
Seepe, P. E.
Stacey, A. E., Jr.
Grantwood —
Butler, P. D.
Powell, K. A.
Priester, G. B.
Bliss, G. L.
Buckley, M. B.
MONTANA
Hackensack —
Pung,^ D. W.
Roberts, J. R.
Rossi ter, P. A.
Caleb, D.
Campbell, E. K.
, Campbell, E. K., Jr.
Big Timber —
Strickland, A. W.
Turnau, E. H.
Haddonfield—
Rowley, F. B.
Chase, L. R.
Dobbs, C. E.
Sanford, A. L.
Schernbeck, F. H.
Steinkellner, E. J.
Clegg, C.
Cook, B. F.
Dawson, T. L.
Billings—
Cohagen, C. C.
Jones, R. E.
Moody, L. E.
Stiller, F. W.
Sunclcll, S. S.
Sutherland, D. L.
Disney, M. A.
Dodds, F. F.
Downes, N. W.
Bozeman —
Powers, F. I.
Hasbro uck Heights —
Goodwin, S. L.
Swanson, R. G.
Eppright, J, O.
Hawthorne —
Sweivcn, C. E.
Swenson, J. E.
Fehlig, J. B.
Filkins, H. L.
NEBRASKA
Lawton, F. C.
Tabor, C. B.
Uhl, K. J.
Flarsheim, C. A.
Gillham, W. E.
Clarks —
Irvington —
Uhl', W. F,
Van Horn, H. T.
Haas, E., Jr.
Kell, W. R,
Manning, W. M.
Freas, R. B.
Reinke, A, G.
Welter, M. A.
Whullon, F.
Whitson, L. S.
Willis, L, JL.
Kitchen, J. H.
Lewis, J. G.
Maillard, A. L.
Matthews, J. E.
Scotts Bluff—
Davis, O. E.
Jersey City —
Hasagen, J. B.
Jones, H. L.
Owatonna—
Millis, L. W,
Natkin, B.
NEW JERSEY
Kelly, C. J.
Ritchie, W,
Clarkaon, W. B.
Nottberg, G.
Nottberg, H.
Arlington —
Schwartz, J.
Walterthum, J. J.
Robbimdale—
Qlchoff, M.
Olson, G. E.
Adler, A. A.
Kearny —
Sweatt, C, H.
Pines, S.
Radio, H. M.
Bock, B. A,
Emery, H.
Holbrook, F. M.
Roches tor—-
Adams, N. D,
Russell, W. A.
Shepparcl, F. A,
Stephenson, L. A,
Asbury Park —
Strevell, R, P.
Lyndhurst —
Ehrlich, M. W.
Shovlln—
Nesdahl, E, ^
Weiss, C. A.
Wymore, F. C.
Zink, D. D.
Atlantic City—
Strouse, S. B.
Maplewood —
Evans, W. A,
Kepler, D. A,
St. Paul-
Maplewood"—
Audubon*—
Kylberg, V. C.
Smith, M. S.
Arnold, E, Y,
Backstrom, R. E.
Walters, A, L.
Sanbern, E. N.
Morchantville —
Bamum, C. R.
Buenger, A,
St. Louia—
Belmar —
Binder, C. G.
Fitta, C, D,
Barry, J, G,, Jr.
Merkel, F, P,
"M + l«l
Gausman, C, E*
GUI, J. w.
Baysc, H, V,
Bradley, K. P.
Bloomfleld—
Bentz, H
Haslett, H, M*
Mickey, D. W.
Carlson, E, E,
Clegg, R. R.
• Hochuli, H. W.
Tenney, D.
Newark-
Hyde, L. L.
Jones, E, F.
Kolinsky, M, D,
Lindberg, A. F.
McNamara, W;
Oberg, H. C,
Penttsi, R,
Boucher, R. C.
$ha*w« H, W.
Cooper, J. W.
Corrigan, J, A*
Davis, C, R,
DuBois, L, J,
Edwards, D. F,
Fagin, D. J,
Farvey, J. D.
Fillo.F. B.
Foster, J. M.
Gilmore, L. A.
Griffin, J. J.
Groasoiann, H* A.
Camden—
Brown, W. M.
Kappel, G. W. A.
Lanning, E. K.
Webster, E. K*
Webster, W,
Webster, W., Jr,
Collinflswood'—
Plum, L, H.
Alt, H. L.
Ashley, C, M,
Bryant, P, J,
Carey, P. C,
Carrier, W. H,
Day, V, S,
French, D.
Holton, J. H.
Ingda, M,
Lelnroth, J. P,
Lewis, L, L.
Lewis, T,
Wtowtorl&fo, M* S,
Hamilton, J, E,
Ba$t Oranfte—
Lvle, J, I.
Matullo, J. R.
tfttfaut1 Oarove—
^IftiQit* 0* J.
Hasten T*. j"
Kent, J. K, \
Langenbem E. B,
Maimhan, J. &
Atldnaon, K. B,
Gombm H," B," ,
Morehouae, H. P,
Rachal, J, M.
Ray, L.B.
Raymfer, W. F,, Jr*
^> It^ySfftiti**"*''*^' ' '
McLeary, H, W.
Racki jS*« C-
Rice, It B.
K&dfya*. C, W,
M€M&i|Qiu T« W*
JL^liy, J* H»
Soule, L. C.
Tallmadge W»
Stelnmetz, C, W, A.
W£^ F.D
Eodei£*l«eVf G. B.
Turno W' G* *W»
WordSam, H.
Tavanlar, E. V,
West, P,
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
North Arlington—
Evans, C. A.
New Rochelle—
Fife, G. D.
Bermel, A. H.
Vogelbach, O.
Farnham, R.
Farrar, C. W.
Gifford, C. A.
Abrams, A.
Farley, W. F.
Finch, S. B.
Fleisher, W. L.
Flink, C. H.
Orange —
Hamlin, C. J., Jr.
Rose, H. J.
Frank, O. E.
Crawford, J. H., Jr.
Harding, L. A.
Heath, W. R.
New York City—
Frey, G. O.
Friedman, M.
Pater son —
Hedley, P. S.
Addams, H.
Galloway, J. F.
Cox. H. F.
Hexamer, H, D.
Ames, C. F.
(Brooklyn)
Pryor F. L.
Jackson, M. S.
Ashley, E. E.
Gautesen, A.
Johnson, E. E.
Atherton, G. R.
(Brooklyn)
Perth Amboy —
Kamman, A. R.
Bachler, L. J.
Genchi, B.
Simkin, M.
Landers, J. J.
Love, C. H.
Balsam, C. P.
(Brooklyn)
(Brooklyn)
Gianm'ni, A. A.
Plainfield—
Madison, R. D,
Barbera, H. A.
Gilmour, -A. B.
Hedges, H. B.
Mahoney, D. J.
Barbieri, P. J.
Glorc,, E. F.
Tobin, G. J.
McTernan, F. J.
Barnum, M. C.
Goldberg, M.
Mosher, C. H.
Baum, A. L.
(Brooklyn)
Ridgefield Park-
Murray, T. F.
Beebe, F. E. W.
Goldschmidt, O. E.
Davis, A. C.
Rente, H. W.
Bennett, E. A.
Gordon, P. B.
Roebuck, W., Jr.
Bennitt, G. E.
Gornston, M, H.
Ridgcwood —
Shelney, T.
Berman, L. K,
Goulding, W.
Pitts, J. C.
Snyder, J. S.
Bernharcl, G
(Brooklyn)
Strouse, S. W.
(Lawrence, L. I.)
Haigney, J. E,
Roselle Park —
Karnpish, N. S.
Thornton, R. T.
Voisinet, W. E.
Bernstrom, B,
Bilyeu, W. F.
(Brooklyn)
Hamburger, F, G,
Walker, E. R.
Blackburn, E. C., Jr.
Hament, L.
South Orange—
Wendt, E. F.
(Hempstead, L. I.)
Hartman, F. S.
Hansen, C. C.
Yager, J. J.
Blackmail, A. O.
Hateau, W. M.
Blackmore, J. J.
Heibel, W. ET
Summit —
Eggertsville—
Blackshaw, J. L.
Henry, A. S., Jr.
Oaks, O. 0.
Teaneck—
Eiss, R, M.
Hirschman, W. F.
(Brooklyn)
Bodinger, J. H.
Bolton, R. P.
Herkimcr, H.
Herty, F, B.
(Brooklyn)
Heebner, W. M.
Elmira —
Bowles, P.
Browne, A. L,
IlerUler, J. R.
(Brooklyn)
Tenafly —
Davis, B. C.
Bruckmann, J. C.
Hiera, C. R.
Redfield, C.
McGlenn, G. R.
Buensod, A, C.
(Great Neck, L. I.)
Bulkeley, C. A.
Hinklc, E. C.
Union City—
Geneva —
Burbaum, W. A,
t(ilempstead, L. I.)
Taverna, F. F.
Herendecn, F. W,
Callaghan, P. F,, Jr.
Hmrichaen, At F.
(Brooklyn)
Hoitman, C, S,
Upper Montclair —
Hamburg —
Callahan, P. J.
Holliater, N, A.
Fernald, H, B., Jr.
Graham, C, H.
(Great Kills, S. I.)
Campbell, F. B,
(Brooklyn)
Hoskina, H. L.
Verona —
Stone, G. F.
Hastlngs-on-
Hudaon— -
Campbell, R. E,
Carpenter, R. H.
Hotchklas, C, H. B,
Howcll, K. B.
West Orange—
Reynolds, T. W.
Charles, T. J,
Charlet, L. W.
Hymun, W. M.
IsBcrteU, H. CJ.
Adlam, T. N,
West New York—
Hudson Falls —
HolHster. E. W.
Chase, C. L.
(Brooklyn)
Cohen, N.
Jacobus, D. S.
Janet, H, L.
Johnson, K. B.
Stinard, R, L.
Irvington-on-
Crone, T, E,
Cucci, V, J,
(W. New Brighton,
S. I.)
NEW YORK
Hudsott—
Bastedo, A. K.
Dailey, J. A,
(Astoria, L. L)
Johnston, W. H.
Kagey, I. B.^Jr.
Ithaca-
Darta, J* A".
Kaufman, W, M,
Albany—-
Barns, A, A,
Daviwn, R, L.
Kenward, S. B,
Anker, G. W.
Sawdon, W. M,
DeBiois, L. A.
(Bay Shore, L. I,)
Bond, H. A,
Johnson, H. S,
Williams, J. W,
Woods, E. H,
Deely, J. J.
(Brooklyn)
Keplinger, W. L.
Kimbafi. D, D.
Ryan, H. J,
Denny, H. R,
Knopf, C.
Taggart, R. C.
J a m es town —
Donnelly, R,
Kuhlmarm, R.
Teeling, G, A,
Sharp, F. H,
Downe, E, R,
Ume, D, D.
Blnfthamton— «• •
Kendall—
Drlacoll, W. H,
Duff, K,
(Jackson Ileightg,
L L)
Brown, R. F.
Martini, 0,
Stangland, B, F,
Durkee, M. E,
Duryea, A, A,
Lefflngwell, R. R.
Lennon. J. O.
Bronxville —
Dornhdra, G* A.
Kenmore— *
Candee, B, C.
G *•*»»« I T
(Belden Point,
City hlftttd)
Dwyer, T. F,
Leupold, H. W.
Lowy, M, R.
Lucke, C. E,
Buffalo—
Beman, M. C.
Booth, C, A,
Cherry, L. A.
rcen, j . j .
Roseberry, J, H.
Larchmont"—
Gaylor, W. S.
(Brooklyn)
Badic, J, G,
Kelts, H, B,
(Brooklyn)
Elliott, If,
Lyle, E. T,
Lyon, P* S,
Ma! man. H,
(GlendaK L, L)
Mandevilk, E, W,
Cheyney, C\ C,
Creasy, R. E.
Criqul, A, A.
Currier, C, H.
Lockport—
Bishop, C. R,
Saunders, L, P,
Engle, A,
Everetts, J., Jr.
Fangler, P. E,
$ay, F, C*
(Brooklyn)
Mariao, & A,
Markush, E. U.
ManhalL H* H,
Danforth, N. L.
Davis.J.
Day, H. C.
Dyer, 0, K,
Erdie, G. F.
Mt, Vemon-~
Kreitag, F. G,
Northon, L,
Obert, C, W.
Fealey, D. R.
Few man, A. M,
Fenner, N, P.
Ferrero, H. L
Fiedler, H, W.
Martia, G, W,
McClotishan, C,
(Brooklytt)
McKlever, W, H.
MeUitfei, W» S,
48
ROLL OF MEMBERSHIP
Mehne, C. A.
Sterne, C. M.
McLenegan, D. W.
Richard, E. J.
Mcinke, H. G.
(Long Island City)
Vogel, A.
Royer, E. B.
Meisel, C, L.
Stewart, C. W.
Welch, L. A., Jr.
Sigmund, R. W.
Meyer, C. L.
Still, F. R,
Smith, J. A.
Meyer, H. C., Jr.
Strock, C.
Snyder —
Sproull, H. E.
Miller, C. A.
Strunin, J.
John, V. P.
Washburn, M. J.
Monroe, M.
Sutton, F.
Winther, A.
Montgomery, 0. C.
Moore, R. E.
(Brooklyn)
(Babylon, L. I.)
Syska, A. G.
Thomson, T. N.
Syracuse —
Acheson, A. R.
Woese, C. F.
Wright, K. A.
Cleveland —
Morse, F. W.
Moss, E.
(Huntington, L. I.)
Tiltz, B. E.
Tarrytown—
Allman, N. S.
Andes, W.
(Brooklyn)
Timmis, W. W.
Abraham, L.
Avery, L. T.
M under, J. F., Jr.
Tisnower, W.
Weiss, A. P.
Bailey, E. P., Jr.
Munier, L. L.
Munro, E. A.
(Brooklyn)
Torrance, H.
Utica—
Brooks, F. W.
Brueggeraan, A. R.
(Lynbrook, L. I.)
Tucker, F. N.
Steinhorst, T. F.
Cohen, P.
Murphy, C. G.
Neale, L. L
(Freeport, L. I.)
Tuach, W.
White Plains-
Conner, R. M.
Davis, J. R.
Neary, D. A.
(Brooklyn)
Johnson, L. O.
Dickenson, F. R.
Offner, A. J.
Tyler, R. D.
Zibold, C. E.
Eveleth, C. F.
O'Hare, G. W,, Jr.
Olsen, G. E.
Vetleaen, G. U.
Vivarttas, E. A.
Williamsville—
Fonda, B. P.
Fox, O.
(Arverne, L. 1.)
(Brooklyn)
Rente, S. R.
Geissbuhler, J. O.
Olvany, W. J.
Osburn, R. M,
Vogt, J. H.
Waechter, H. P.
Yonkers —
Gottwald, C.
Graham, W. D.
Pabst, C. S.
Patorno, S. A. S.
(Thompkinsville,
S. L)
Archdeacon, H. K.
Bense, W. M.
Harvey, L. C.
Hendrickson, J. J.
Pfuhler, J. L.
Wachs, L. J.
Brabbe6, C. W.
Kalinsky, A. G.
(W. New Brighton,
(Brooklyn)
Deutchman, J.
Kartorie, V. T.
S. L)
Wagner, F. H., Jr.
Goerg, B.
Kitchen, F. A.
Phillips, F. W., Jr.
Walker, W. K,
Hayter, B.
Klie, W.
(Brooklyn)
Wallace, G. J.
Kelly, J. G.
Levy, M. 1.
Pihlman, A. A.
(Elmhurst, L. 1.)
Rainger, W. F.
Martinka, P» D.
Pinder, P. H.
Wallace, W. M,, U
Stitt, A. B.
Matzen, H. B.
Place, C. R.
(Hollis, L. I.)
Zuhlke, W. R.
O'Gorman, J. S.r Jr.
Pohlc, K, F.
Walton, C. W., Jr.
Miles, J. C.
Presdee, C. W.
Price, K. H.
Waring, J. M. H.
White, E. S.
NORTH CAROLINA
Prendergast, J. J,
Quinlivan, L. P.
(Rivcrhead, L. 1.)
Whitdaw, H, U
Rather, M. F.
Purdy, R. B.
Wilder, K. L.
Charlotte —
Repko, J. J.
Purinton, D. J.
Wilson, H. A., Jr,
Brandt E. H.
Schick, K. W.
Quigley, W. J.
Uuirk, C. H.
Raffes, A.
Winquiat, W. J.
(Brooklyn)
Wohi, M, W.
Christian, C. W.
Hodge, W. B.
Small, B. R.
Schmidt, R. H.
Schurman, J. A.
Sennet, L. E.
Raislcr, R. K.
Spencer, R. M,
Raynis, T.
Oriskany -
Hi&h Point-
Steffner, E. F.
(Woodhaveu L. 1.)
Reed, J. K.
Oakey, W. K,
Gray, W. E.
Tuve, G. L.
Vanderhoof, A. L.
Reynolds, W. V.
Ossluin& —
Winston - Salem ~—
WetzelU H. E.
Richardson, H. T.
Hooper, V. F.
Bahnson, F. F,
Wilhelm, J. E.
Riley, C. L,
Riley, R. C. »
(Jamaica, L, I.)
Patchoque —
Jalonack, I. G.
Turner, M. E.
NORTH DAKOTA
Wise, D. E.
Cleveland Height*—
Ritchie, E. J.
Davis, R. G.
Ritter, A.
Pelham Manor
" -i"-'"m-~-
Rodgers, F. A.
Rodman, R. W,
Rosenberg, P.
Peacock, J. K.
Grand Forks —
Pesterfield, C. H.
Columbus-
Rosa, J. 0.
Port Jorvis—"
Brown, A, L
Roth, C, F.
Rozettv W*, Jr,
Trimmer, C. M,
OHIO
Sherman, R. A.
Slayter, G,
Ruppert, E. H,
Rochester--*
-—""•"•-'—'
Wheeler, O. J.
Schneider, W, G,
Schoepiiia, P. H,
Schulze. B. H.
Scott, d E,
Betlam, H. T.
Coe, R. T.
Cook, R. P.
Hakes, L. M.
Belief on taine —
Quay, D. M.
Berea—
Williams, A, W.
Cuyahoga Falls-
Humphrey, D. E,
Scott, G* M,
Scribner, E. D.
Seelbach, H.
Seelig, A. E,
Sell man. N. T,
Hutchina, W. H.
Sheldon, N. E,
Stacy, S. C,
Welah, H, S.
Curtii, H. F.
Cincinnati—-
Bird, C.
Dayton-
Hull, H, B,
LaSalvia, J, J.
Moore, H. W.
Senior, L L.
Seward, P. H.
(Brooklyn)
Shepard, E* C.
Siebs, C, T,
Rome—
Lynch, W. L,
Steels, M. G.
\ Breneman, R. B.
Buford, J. W.
Coombc, J.
Doyle, W, J.
Floyd, M.
Williams, F, H.
East Cleveland*-
Morria, F. H,
' Nobia, H. M.
Scarsdaltt —«
Green, W. C,
Read, R, R,
(Brooklyn) '
Skidmore, J. G.
(Long Island City)
Sklemrik, L,»
Stack, F. C.
(Flushing, L. I.)
Staples, W. H,
S^srnberg, E.
Curnmlng, R. W.
Uliraan, H* G.
Cannon, C. N,
Fauat, F. H.
Harrington, E, D.
Hunssiker, C, E.
James, J. W*
Helburn, L B.
Houliston, G, B.
Hust, C. E,
Kiefer, C. J,
Kitchdl, H. N.
Kramlg, R, E., Jr,
Hllen, H. A,
Pistler, W. C,
Powera, L. G.
Stark, W. E.
ElyrJa—
Maynard, J. E.
Lakewood —
I*ongcoy, G, B,
Ramsey, R. F,
Vermere, E. J.
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
Mansfield —
Beech wood, Del. Co.~
Philadelphia-
Wilmot, C. S.
Yardley, R. W.
Kipe, J. M.
Adams, B.
Bartlett, C. E,
Woolston, A. H.
Wright, M. B.
Newark —
Bradford —
Black, H. G.
Pittsburgh —
Simpson, D. C.
Black, W. B.
Blankin, M. F.
Aston, J.
Norwood —
'Braun, J. J.
Motz, O. W.
Butler —
Karges, L.
Bogaty, H. S.
Bornemann, W. A.
Braemer, W. G. R.
Breitenbach, G. C.
Beighel, H. A.
Blackmorc, G. C.
Blackmore, J. S.
Caldwell, A. C.
Brauer, R,
Painesville —
Ghambersb ur & —
Cassell, j. D.
Burns, J. R.
Hobbs, J. C.
Kottcamp, H. A,
Clarkson, R. C., Jr.
Clodfelter, J. L.
Bums, R.
Bushnell, C. D.
Shaker Heights —
Bolz, H. A.
Gary, E. B,
Steubenville —
Smith, R. H.
Cheltenham —
McElgin, J. W.
Cynwyd —
Smith, W. F.
Cornell, J. C.
Culbert, W. P.
Dambly, A. E.
Davidson, L. C.
Davidson, P. L.
Donovan, W. J,
Eakins 'W'
Carr, M. L.
Cheeseman, E. W.
Collins, J. F. S., Jr.
Comstock, G. M.
Dice, E. vS.
Dorfun, M. I.
Edwards, P. A.
Toledo-
E. Pittsburgh —
Eggly, H. J., Jr.
Evans, E. C.
Frit? (7 V
Baker, H. C.
Goodwin, W. C.
Eichberg, W. R,
Giles! A! F.'
Myers, F. L.
Treadway, Q.
Youngstown —
Boucherle, H. N.
Chomn, C. C.
Elizabethtown —
Dibble, S. E.
Erie-
Joyce, H. B.
Elliot, E.
Engel, E.
Erickson, H. H.
Faltcnbacher, H. J.
Kamiletti, A, R.
Galligan, A. B,
Gant, H. P.
Gunther, F. A.
Hecht, F. II .
Heilman, R. H.
Hickey, J. W.
Houghten, F. C.
Humphreys, C. M.
Huettner, 1L F.
OKLAHOMA
Glenolden —
Grossman, H. E,
Harrisburg. —
Eicher, H. C.
Geiger, L H.
Lutz, J. H,, Jr.
Oilman, F.' W.
Glaasey, J. W.
Hackett, H. B.
Hibbs, F. C.
Hires, J. E.
Hoft, P. J.
Hunger, R. F.
Ingold, J, W,
Kellner, D* C.
Kennedy, O, A.
Kennedy, P, V.
Lofte, J. A.
LuU, W. J.
Muclilinjs, L. S.
Msxjjinii P. 1^«
Bartlesvllle—
Yates, G. L.
Norman —
Bowman, J. W.
Chestnutt. N. P,
Cook, A. B.
Dawson, E. F.
Frarapton, A. C.
Husky, S. T.
McKinley, C. B.
Haverford—
Black, E. N., 3rd
Jenkln to wn—
Slight, I.
Hynca, L, P.
Ickeringill, J. C,
Jellett, S. A.
Kclble, F, R.
Kriebel, A. E.
Leopold, C. S.
Lewis, G. C.
McGinncjBS, J. E.
MeDonagle, A.
McGuigan, L. A.
Mdntush, F. C,
McMunn, A. H.
Miller, K. A.
Nn."W A V
Rauh, E. M.
Sneed, R. B.
Sonney, K. J.
Johnstown —
Novotney, T. A.
MacDade, A. H,
Mann, L. B.
Marks, A. A.
Nicholla, P.
Nordheiu\cr, C, L,
O'Neill P,
Oklahoma City-
Stitt, E. W.
Martocello, J. A.
Mather, H, II.
Oatcrle! W. H.
Beard, E. L.
Dolan, R. G.
Dugger, E. R.
Kingston —
MacDonald, D. B.
McClintock, A., Jr.
Mellon, J. T, J.
Menaing, F. D,
Pierce,' W. MacL.
Pittock, L. B.
Reed I G
Emmons, N. L.
Gray, B. W.
Hewlett, I. G,
Loeffler, F. X,
Loemer, L,, Jr,
Miller, B, R,
Miner, M. H,
Rathbun, P. W.
Holland, S. L.
Tauson, P. 0*
Tiller, L.
Tulsa—
Burke, W. J,
Jones, E.
Lancaster —
e'nea, A.
oyd, E. C,
Long, D, R.
Lan sdo wne —
Hansen, C. J.
James, H. R,
Manheim—
Weltzel, P. H,
MaryavUle—
Gault, G. W,
Meyer, J, W,
Monday, C. E.
Morgan, R. C,
Morris, A. M,
Naylor, C, L,
Neabitt, A. J.
Neabitt, J. J.
Newcornb, L. B.
Nusbaum, L,
Flaw, C. W.
Plewea, S. E,
Powers, E, C.
Pryibil, P, L.
Redstone, A, L,
Rellly, C. E.
Reed! V, A.
Richmond, J,
Riddle, K. L,
Rlesmeyer, E, H., Jr.
Rockwell, T, R
Seanlon, K. S.
Smyers, 1C, C.
Speller, K, N.
Stanger, R, B,
Steen, J, M,
Steggall, H. B,
Stevenaon, W» W.
Strauch, P. C,
Tennant, R» J, J,
Tower, E, S,
OREGON
McKeesport"—
Duuan T M
Ret tew. H, F.
Rhea, C. A.
Roberts, H. L,
Waters, G, G,
Wright, C E,
Rugart, 1C,
Corvallis—
Meftdvllle—
Sabin, E, R.
Marty, E( 0.
WiHey, E, C,
Williams, L, E,
Shanklin. A. P.
ShelHer, M.
Smith, J, D,
PENNSYLVANIA
Merlon-
Atkins, T, J,
Speckman, C. H,
Stevens, J, M.
Thornburg, H. A,
Tiramls, P.
Luck, A, W,
.Nicely, J. E,
Rldtey X»*irk—
Allen town—*
Korn, C. B.
New Castle-
Andrews, G. H.
Touton, R, D.
Traugott. M,
Mawby, P,
Stalb, J, G*
Ardmore—
Haynes, C, V,
Sonneborn, C.
Norristown— *
Trump, C. C,
Tuckerman, G* E.
Walsh, J. A,
Rutledfte—
Vroom«, A, E.
Jteaver Falls-—
Bolsinger, R, C.
Wandi«u«, F. W*
jS^gnUktOXI'***'
Vfcji Atan, W, T.
Hucker, J, H.
Wegraann, A.
Sbnyer, H» E*
50
ROLL OF
MEMBERSHIP
State College-
TEXAS
Portsmouth —
Ft. Atkinson —
Queer, E. R.
Stubbs, W. C.
Shodron, J. G.
Stroudsburg, —
Amarillo —
Richmond —
Kohler—
Kiefcr, E. J., Jr.
Burnett, E. S.
Carle, W. E.
Hvoslef, F. W.
Tamaqua —
Hadesty, A. L., Jr,
Koch, H. O.
College Station —
Badgett, W. H.
Giesecke, F. E.
Smith, E. G.
JcJhnston, J. A.
Livingston, B. B.
Pelouze, H. L., 2nd
Schulz, H. I.
Snyder. A. K.
Kohler, W. J., Jr.
LaCrosse —
Anderegg, R. H,
Miller, M. W.
Upper^Darby —
Eastman, C. B.
Taliaferro, R. R.
Dallas —
Bock, I. I.
Boruch, E. R.
University —
Peebles, J. K., Jr.
Trane, R. N.
Madison —
Villanova —
Ban-, G. W,
Durning, E. H.
Gay, L. M.
Landauer, L. L,
WASHINGTON
Dean, C. L.
Hess, D. K.
Larson, G. L.
Carey, J. A.
Wallin&ford—
Lynn, J, H.
Meffert, G. H.
Witmer, C. N.
Kent—
Boyker, R. O.
Nelson, D. W.
Plaenert, A. B.
White, J. C.
Arnold, R. S,
Ft. Worth —
Pullman —
Menomonie —
Wilkes-Barre—
Skinner, H. W.
O'Connell, P. M.
Schoenoff, A. E.
Santee, H. C.
Houston —
Seattle —
Milwaukee —
Wilkinsburg—
Groseclose, J. B.
Beggs, W. E.
Berghoefer, V. A.
Campbell, T. F,
Vernier, M. G.
Kiesling, J. A.
Renouf, E. P.
Bouillon, L.
Cook, H. A.
Bowers, A. F,
Bowers, R. C.
T
Cox, W. W.
Brown, W. H.
WWiamsport—
Irving —
Daly, C. P.
Burch, L. A.
Pfeiffer, J. F,
Moler, W, H.
Dudley, W. L.
Elliott, N. B.
Wor mlcy sb ur ft —
Miller T. G.
Kin&ssviile~—
Richtmann, W. M.
Eastwood, E. O.
Forsyth, A. T.
Cranston, R. 0.
Ellis, H, W.
Freeman, A. M.
Hanley, E. V.
York-
Baker, L C.
San Antonio—-
Diver, M, L.
Ebert, W, A.
Griffin, D. C.
Hauan, M. J.
Hendrickson, H, M.
MacLeod, K. F.
Haupt, H. F.
Herrmann, H. C.
Jackson, C. H.
Jepertinger, R. C.
RHODE ISLAND
Sherman —
Mallis, W.
May, C* W.
Jones, E. A,
Jung, J. S,
, J.__,,Jtll,m-.J,
Reynolds, J. A,
Musgrave, M. N.
Juttner, O. J.
Providence—
UTAH
Peterson, S. D.
Pollard, A. L.
Miller, C. W.
Miller, H. M.
Coleman, J. B.
ji_.^...>.
Twist, C. F.
Noll, W. F.
Gibba, E, W.
Hartwril, J. C.
McLaughlin, J. D.
Moulder, A. W,
Salt Lake City —
Richardson, II. G.
Zokell, C. G.
Tacoma —
Spofforth, W.
Peters, H, H.
Randolph, C. H.
Rice, C. J,
Shawlin, W. C,
SOUTH CAROLINA
VERMONT
Yakima—
McCune, B. V.
Spence, M, R.
Spielmann, H. J.
SwJsher, S. G., Jr,
——-—'—
Burlington —
Szekely, E.
Caaey, 11. F.
Lanou, J. E.
Raine, J, J,
WEST VIRGINIA
Volk, J. H.
Wagner, A, M.
Clemaon Colle&e—
North Fentisburft—
1 Charleston —
W?lso"'W.' H!
Shenk, D. H,
Breckenrldge, L, P.
Shanklin, J. A.
Racine — •
TENNESSEE
VIRGINIA
Thompson, D,
Titus, M. S.
Dixon, A. G,
Thomas, N. A.
Memphis—
Danville-
Larftent™—
Donnelly, J, A,
Superior —
Campbell, A. Q,, Jr,
Farley, W. S,
Innis, H, R.
Waite, H.
D'Imor, B. J.
Hoshaii, R, H.
Perkins, R. C,
Lynchburg —
Doering. F, L*
Wiley, E. C.
WISCONSIN
Wauwatosa —
Page, H. W.
Nashville™""
H rowxi F«
Norfolk—
Ashland —
West Allls—
Jarrett, P. R.
Nowitsky, H, S.
Trulson, A, F.
Erickson, M. E.
51
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
FOREIGN COUNTRIES
AUSTRALIA
Eaton, W. G. M.
ENGLAND
Ellis, F. E.
Sydney —
Duncan, J. R.
Hunt, N. P.
Sands, C. C.
Flanagan, E. T.
Gaby, F. A.
Gurney, E. H.
Harrington, C.
Heard, R. G.
Buckinghamshire—
Russell, J. N.
Leeds —
BELGIUM
Henion, H. D.
Jennins, H. H.
Hills, A. H.
Hopper, G. H.
Jenney, H. B.
Leitch, A. S.
London —
Bailey, W. M.
Butt, R. E. W.
Brussels —
Mautsch, R.
CANADA
MacKenzie, J. J.
Marriner, J. M. S.
Greenland, S. F.
Haden, G. N.
Brandon, Man. —
McDonald, T.
McHenry, R. W.
Herring, E.
Nobbs, W. W.
Yates, J. E.
Millar, R. J,
Moore H S
Middlesex-
Brockville, Ont. —
O'Neill, J.' W.
Case, W. G.
Davenport, R. F.
Paterson, J. S.
Chipperfield, W, H
Calgary, Alberta-
Paul, D. I.
Philip, W.
Stockport —
Clarke, S. S.
Playt'air, G. A.
Webb, J. W.
Walker. A.
Price, D. O.
Edmonton, Alberta-
Purdy, A. K.
Ritchie, A. G.
Sutton —
Casperd, H. W. H.
Kelly, H.
Roth, H. R.
Shears, M. W.
Swinton —
Gait —
Sheppard, W. G. F.
Yates, W.
Oke, W. C.
Sheldon, W. D., Jr.
Thomas, M. F.
Waldon, C. D.
Trowbrid&e —
Halifax, N. S.—
Watson, M. B.
Whittall, E. T,
Haden, W. N.
Eagar, R. F.
Woollard, M. S.
Westminster —
Hamilton, Ont.—
Wood, J. S.
Faber, Dr. O.
Best, M. W.
Vancouver, B. C.~~
Wolvorhampton— •
Fitzsimons, J. P.
Johnston, R. E.
Tyson, W. H.
Maddux, O. L.
Leek, W,
Pennock, W. B.
Libby, R. S.
FRANCE
McCreery, H. J.
Islington, Ont.- —
Wilson, G. T.
Victoria, B. C. —
Dijon-
Kitchener, Out. —
Sheret, A.
Bur, J. R. C,
Beavers, G. R.
Wellington, Out.™—
Lille—
Montreal, P. O. —
Johnston, H. D.
Neu» H. J. E.
Darling, A. B,
Winnipeg Man.—
Lyon —
Fogarty, Q. A.
Glass, W.
Goenaga, R. C.
Friedman, F. J.
Jones, B. G.
Garneau, L.
Kirk, C. D.
Paris—
Givin, A. W.
Leonard, J. H.
Beaurrienne. A,
Johnson, C. W.
Michie, D, F,
Downe, H, S,
McGrail, T, K,
Steele, J, B.
Modiano, R.
Osborne, G. H.
Summers, E. T,
Nessi, A,
Phipps, F. G,
Turland, C. H,
Schmuts!, J.
Wiggs, G. L.
Montreal, W., P» Q.—
CHINA
GERMANY
tinton, J. P. -
Nanklnft—
Berlin—
Ottawa, Ont,—
Loo, P. V,
Brand!, O, H,
Colclough, O. T*
Gray, G. A.
Shanghai—
Stutt&art—
Ke&ina, Sask. —
Stewart, J. C,
Carter, D,
Doughty, C. J.
Hart- Baker, H* W,
Klein, A,
HOLLAND
Kwan, 1. K.
Three Rivers, Que.—
Germain, Q,
Toronto, Ont.—
Loh, N, S.
Merritt, C, J.
Morrison, C, B.
Waung, T. F,
Amsterdam —
Overton, S, H.
Allsop, R. P.
Angus, H. H.
CZECHOSLOVAKIA
INDIA
Anthe& L JL
Arrowsinith, J» O,
Praa—
New Delhi-
Bfrrell, A. L.
Blackball, W. R.
Brust, 0.
Heard, J, A. E.
Boddington, W, P,
Church, H, J,
DENMARK
IRELAND
Cole, G* E.
Dickey, A, J.
Copenhagen*—
Cork-
Duncan, W, A,
Reck, W, K>
Barry, P. I.
ITALY
Milan—
Donzelli, E,
Gini, A.
Hauss, C. F.
JAPAN
Osaka —
Fukui, K.
Tokyo*—
Kitaura, S.
Kozu, T.
iSaito, i>.
yekido, K,
MEXICO
Lomas de
Chapul tepee —
Gilfrin, G. F.
Mexico, D. P.—
Darby, M. 11.
Martinez, J. J.
NEW ZEALAND
Ghristchurch —
Taylor, K. M,
Vale, H, A, L,
Dimedln —
Daviea, G. W.
NORWAY
Oslo-
All sen, N.
TjeralunU, A,
PHILLIHNK
ISLANDS
Moloiloilo—
Piion, D., jr.
SOUTH AFRICA
J ohannesb ur & - •
Carrier, E. G.
SWEDEN
Ro«ell, A, F,
Stockholm-
Gille, H.
TheorelU H, G, T.
, M. L,
SCOTLAND
Dundee-—
Knoxf J, E.
PAST OFFICERS
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS
1894
President Edward P. Bates
1st Vice-President Wm. M. Mackay
$nd Vice- President Wiltsie F. Wolfe
3rd Vice-president Chas. S. Onderdonk
Treasurer Judson A. Goodrich
Secretary L. H. Hart
Board of Managers
Chairman, Fred P. Smith
Henry Adams A, A. Gary
Hugh J. tturron James A. Harding
' " " ~ L. H. "
Edward P. Hates, Prcs.
. Hart, Secy.
Council
Chair man » R, C. Carpenter
Albert A. Cry^r Chas. W. Newton
F, W* Foster Ulysses G. Scollay, Secy.
1897
President Wm. M. Mackay
1st Vice-President H. D. Crane
8nd Vice-President Henry Adams
Srd Vice-President A. E. Kenrick
Treasurer Judson A. Goodrich
Secretary H. M. Swetland
Board of Managers
Chairman, R. C. Carpenter
Edward P. Bates Stewart A. Jellett
W. S. Hadaway, Jr. Wiltsie F. Wolfe
Wm. M. Mackay, Pres. H. M. Swetland, Secy.
John A. Fish
Wm. McMannis
Council
Chairman, Albert A. Cryer
James Mackay
B. F. Stangland
1895
President...... , ..........................Stewart A. Jellett
1st Vic,f -President...,, Wm. M. Mackay
Snd Vice-president. ,...Chaa. S, Onderdonk
3rd Vice-President ......D. M, Quay
Treasurer............ , Judson A. Goodrich
Secretary.., .,.. „ L, H. Hart
Board of Managers
Chairman, Jaraea A, Harding
Ceo. B, Cobb Ulysses G. Scollay
Wm. McMannis B. F. Stangland
Stewart A, Jellett, Pres. L. H, Hart, Secy.
Council
Chairman, R, C. Carpenter
Henry Adama T, J. Waters
Edward P. Batei Albert A, Cryer, S««y«
1898
President........ Wiltsie F. Wolfe
1st Vice-President T. H. Kinealy
Snd Vice-President A. E. Kenrick
Srd Vice-President.^ ...John A. Fish
Treasurer. Judson A. Goodrich
Secretary. ...Stewart A. Jellett
Board of Managers
Chairman, Wmu M. Mackay
Thomas Barwice A. C, Mott
John A, Connolly Francis A. Williams
Wlltalc F. Wolfe. Pres. Stewart A. Jeliett, Secy*
Council
Chairman, R. C, Carpenter
Henry Adams W» S, Hadaway, Jr.
Albert A* Cryer Wm, McMannis
Wllttle F, Wolfe, Fm. Stewart A, Jeilett, Secy.
.......... ................. ..», .......... ...R. C. Carpenter
Xst Vice-president, ...... ......,«.....,....,.......,.D. M, Quay
Viti-Pr*sident»mt..»f» ........ .....Edward P* Bates
$rd
»mt..»f» ........ ..... *
.»~ ....... ............. ..... ....F, W. Foster
.,„ Jfudion A, Goodrich
.M.^..»M......<»»L. H, Hart
Board of Managers
Chairman, Wm. M. Mackay
Hugh J. Barron Stewart A* Jellett
W/k Hadaway, Jr. Wilt* F, Wolfe
E, C, Carpenttr» Pfe*» U H, Hart, Seey.
Council
Chairman, A, A, Cary
Albtrt A, Cry«r B* F. Staaglautd
W». McMnnnls J. J»
1899
Presidtint,..^ ...... ...„.,...»„.„........ ........ .....Henry Adams
1st Vic^PresMent.^..^ ........ ..,..„. ........... D, M. Quay
&nd Vice-President.^.., ............... . ......... A, E, Kenrick
9fd Vice-president ........ ., ........ ....Francis A, Williams
.^ ............ „.„ ............. Judson A. Goodrich
., ...... ...... .............. ».,......Wft* M. Mackay
Board of Managers
Chairman, Stewart A, Jellett
B. H. Carpenter Wm, Kent
A* A. Cary Wtttale F, Wolfe
Htnry Adams, Prttt Wm. M. Mackay, Secy,
Council
Chairman, R» C. Carpenter
John Gormly Wm, McMarmU
W. 8» Hadaway, Jr, B, F, Stangland
Henry Adam«t jPrw* Wm. M, Mackay, Secy.
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
1900
President „ D. M. Quay
1st Vice-President A. E. Kenrick
2nd Vice-President Francis A. Williams
Treasurer Judson A. Goodrich
Secretary Win. M. Mackay
Board of Governors
Chairman, D. M. Quay
Wm. Kent, Vice-Chm. D. M. Nesbit
R. C. Carpenter C. B. J. Snyder
John Gorrnly Wm. M. Mackay, Secy,
1901
President J. H. Kinealy
1st Vice-president A. E. Kenrick
2nd Vice-President^ Andrew Harvey
Treasurer Judson A. Goodrich
Secretary. Wm. M. Mackay
Board of Governors
Chairman, J. H. Kinealy
Wm, Kent, Vice-Chm. John Gormly
R, C. Carpenter C. B. J. Snyder
R. P. Bolton Wm. M. Mackay, Secy.
1902
President A. E, Kenrick
1st V^ce- President Andrew Harvey
Snd Vice-President Robert C. Clarkson
Treasurer. , Judson A, Goodrich
Secretary ..Wm. M, Mackay
Board of Governors
Chairman, A. E. Kenrick
John Gormly, Vice-Chm. J, H. Kinealy
R. C, Carpenter C, B. J. Snyder
Wm. Kent Wm, M. Mackay, Secy.
1905
President Wm. Kent
1st Vice- President R. P. Bolton
Snd Vice-President C. B. J. Snyder
Treasurer Ulysses G. Scollay
Secretary Wm. M. Mackay
Board of Governors
Chairman, Wm. Kent
R. P. Bolton Tames Mackay
C. B. J. Snyder B. F, Stangland
B. H. Carpenter J. C, F. Trachsel
A, B. Franklin Wm. M. Mackay, Secy*
1906
President , John Gormly
1st Vice-President C. B. J. Snyder
2nd Vice-President T. J. Waters
Treasurer Ulysses G. Scollay
Secretary , Wm. M, Mackay
Board of Governors
Chairman, John Gonnly
C. B. J. Snyder, Vice-Chm. Jamea Mackay
R. C. Carpenter B. F. Stangland
Frank K. Chew T, J. Waters
A. B. Franklin Wm, M. Mackay, Secy*
1907
President,.....,. , ,C. B. J. Snyder
1st Vice-President....,,.....,.,......,., James Mackay
2nd Vice-president ......,....Wm. G, Snow
Treasurer..... .„„.„ Ulysses G, Scollay
Secretary ........ Wm. M, Muckay
Board of Governors
Chairman, C. B. J, Snyder
Jamea Mackay, Vice-Chm^ Frank K. Chew
R. E. Atkinson A. B. Franklin
R. C. Carpenter Wm. G. Snow
Edmund F, Capron Wm. M. Mackay, Stcy.
1903
President H, 0. Crane
IstV^e-Presidmt Wm. Kent
£nd Vice-President R. p. Bolton
Treasurer Judaon A. Goodrich
Secretary.^...,.......,. ...........Wm. M. Mackay
Board of Governors
* •« * ^ Chairman, H. D, Crane
C. B. J. Snyder, Vie+Chm* A, E. Kenrick
R, C, Carpenter Geo. Mehring
John Gonnly Wm, M. Mackay, Secy,
1908
President — ............. ..... ...... . ....... , ......... James Mackay
1st Vict-President .......... ,......„„..,... . Jas. D, Hoffman
$nd Vice-President.^ ____ .......... ...... ..., B. F. Stangland
Treasurer ................. ..... ........ ... ....... Ulysses G, Stollay
Swyda/y.......................... ....... ...... ...Wm. M. Mackay
Board of Governors
Chairman, James Maekay
Jas, D.Hoff man, Vic*-Chm. John F, Hale
B, F. Stangland August Kchm
R. C, Carpenter C, B, j,
Frank K. Chew Wm,
, j, Snyder
, M. Mackay,
1904
„.»,.„. Andrew Harvey
-•-• - ,v -•""-- — ...John Gormly
end Vic^President .....Robert C. Clarkson
Treasurer ; .........Ulysses G. Scollay
Secretary., ...,.,.Wm. M. Mackay
Board of Governors
Chairman, Andrew Harvey
John Gormly H. D. Crane
Robert C. Clarkson A, E. Kenrick
J. J, Biackmore C* B, 1 Snyder
R. C. Carp«ntttr Wm, M. Mackay, S#ey.
1909
President..
1st Wc^^«*irf^.I..7.7/,...Z.
Snd "" " '"
Secretary.* "...".".
...,.Wm. G, Snow
August Kehm
.........B* 5. Harriioii
I. Mackay
Board of Governors
Chairman,
August K«hm» Vice-Ckm.
John R, AUen
R. C» Carpfent«r
B. S. H&riiio»
G,
Samuel R. L«wl§
Jfttn«» Mactoy
B» F. &ta,$dam<!
Wia* M. Mwfcity,
ROLL OF MEMBERSHIP
1910
President Jas. D. Hoffman
1st Vice-President R. P. Bolton
£nd Vice-President.^ Samuel R. Lewis
Treasurer Ulysses G. Scollay
Secretary..,..,.. , Wm. M. Mackay
Board of Governors
Chairman, Jas. D. Hoffman.
R. P. Bolton, Vice-Chm. John F. Hale
•Geo. W. Barr Samuel R. Lewis
R. C. Carpenter James Mackay
Judson A. Goodrich Wm, M. Mackay, Secy.
1911
President..,. R, P. Bolton
1st V+CG-Presidcnt John R. Allen
£nd V ice-President..., A. B, Franklin
Treasurer ..Ulysses G. Scollay
Secretary Wm. W, Macon
Board of Governors
Chairman, R. P. Bolton
John R. Allen, Vice-Chm. A. B, Franklin
John T. Bradley Jas. D. Hoffman
R. C. Carpenter August Ivehm
James H. Davis Wm, W. Macon, Secy.
1912
President „ , John R. Allen
1st Vice-President^ John F. Hale
Snd Vice-President Edmund F. Capron
Treasurer , James A. Donnelly
Secretary .....,..., „ Wm. W, Macon
Board of Governors
Chairman, John R. Allen
John F, Hale, Vice-Chm. D wight D, Kimball
Edmund F. Capron Samuel R, Lewis
R. P, Bolton Wm. M. Mackay
Jas. D, Hoffman Wm. W« Macon, Secy.
1913
,,.*.,*,,,,..., John F. Hale
1st Vice-president ,...,...A. B, Franklin
&nd Vice-President ..Edmund F. Capron
Treasurer, ».,», ..„.„., ...James A. Donnelly
Secretary,*,, „....„„......,...... Edwin A. Scott
Board of Governors
Chairman, John F, Hale
A. B. Franklin, VicihChm, James A. Donnelly
John R, Allen Dwight D, Kimball
Edmund F, Capron Wm. W, Macon
R, P, Bolton lames H. Starmard
Frank T» Chapman Theodore Wdnahank
Ralph Collamore Edwin A, Scott , Secy,
£nd
1914 »
,M...WM,M»«. .Samud R, Lewli
^.................Edmund F. Capron
L.; ..... Dwight D, Kimball
„...,.„.»..*..., Jamta A, Donnelly
,««.,*,,...»,.».,.„,„ J. J, Blackmore
Council
Chairman. Samuel R. Lewis
John IL Alien
Frank T* Chapman
Frank I* Cooper
, Donnelly
1915
President Dwight D. Kimball
1st Vice-President Harry M. Hart
Snd Vice-President Frank T. Chapman
Treasurer Homer Addama
Secretary J. J. Blackmore
Council
Chairman, Dwight D. Kimball
Harry M. Hart, Vice-Chm. Samuel R. Lewis
Homer Addams Frank G. McCann
Frank T. Chapman J. T. J. Mellon
Frank I. Cooper Henry C. Meyer, Jr.
E. Vernon Hill Arthur K. Ohmes '
Wm. M. Kingsbury J. J. Blackmore, Secy.
1916
President Harry M. Hart
1st Vice-President Frank T. Chapman
Snd Vice-President Arthur K. Ohmes
Treasurer.^ Homer Addams
Secretary Casin W. Obert
Council
Chairman, Harry M, Hart
F. T. Chapman, Vice-Chm, Dwight D. Kimball
Homer Addams Henry C. Meyer, Jr,
Charles R. Bishop Arthur K, Ohmes
1 Frank I, Cooper Fred R. Still
Milton W. Franklin Walter S, Timmis
E. Vernon Hill Casin W. Obert, Secy.
1917
President , J. Irvine Lyle
1st Vice-President, Arthur K. Ohmes
Snd Vice-President Fred R. Still
Treasurer,, * -.*...» Homer Addama
Secretary.., , Casin W. Obert
Council
Chairman* J. Irvine Lyle
A. K. Ohmee, Vice+Chm. Harry M. Hart
Homer Addama E. Vernon Hill
Davis S. Boyden Jamee M. Stannard
Bert C, Davia Fred R. Still
Milton W. Franklin Walter S. Timmia
Charles A. Fuller Casin W. Obert, Secy.
President.~~~,..* «
J8wd! Wc*-PywW*w/»
Tr«fljttr^.
5«<T«fafy....
1918
„..„ ............Fred R. Still
..... Walter S* Timmis
,.,., E. Vernon Hill
.Homer Addams
.Ctain W, Obert
Council
Chairman, Fred R, Still
W. S. Timmis, Viw-Ckm* J, Irvine Lyle
Homer Addams « E, Vernon Hill
William H, Drtacoll Frank G, Phegley
Howard H, Fielding Fred. W, Power*
», Oant Charaplain k, Eilty
W. Kiwbatt Ca«ta W. Obert» 5#c
AMERICAN SOCIETY of HEATING and VENTILATING ENGINEERS GUIDE, 1935
1919
President Walter S. Timmis
1st Vice-President E. Vernon Hill
2nd Vice-President Milton W. Franklin
Treasurer.^ Homer Addams
Secretary Casin W. Obert
1923
President H. P. Gant
1st Vice-President Homer Addams
2nd Vice-President E, E. McNair
Treasurer Wm. H. Driscoll
Secretary C, W. Obert
Council
Chairman, Walter S. Timmis
E. Vernon Hill, Vice-Chm. Frank G. Phegley
Homer Addaras Fred. W. Powers
Howard H. Fielding Robt. W. Pryor, Jr.
Milton W. Franklin Champlain L. Riley
Harry E. Gerrish Fred R. Still
George B. Nichols Casin W. Obert, Secy.
Council
Chairman, H. P. Gant
Homer Addams, Vice-Chm. E. S, Hallett
W. H. Carrier Alfred Kellogg
T. A. Cutler Thornton Lexvis
S. E. Dibble E. E. McNair
Wm. H. Driscoll Perry West
Casin W. Obert, Secy.
1920
President.. E. Vernon Hill
1st Vice-president Champlain L. Riley
2nd Vice-President Jay R. McColl
Treasurer,^ Homer Addams
Secretary Casin W. Obert
1924
President Homer Addams
1st Vice-President , S. E. Dibble
2nd Vice-President William H. Driacoll
Treasurer Perry West
Secretary..... F. C. Houghten
Council
Chairman, E. Vernon Hill
C. L. Riley, Vice-Chm. Jay R. McColl
Homer Addams Ge< ""
Jos. A, Cutler
Wm. H. Driscoll
A. C, Edgar
Alfred Kellogg
:orge B. Nichols
Robt. W. Pryor, Jr.
W. S. Timmis
Perry West
Casin W. Obert, Secy.
Council
Chairman. Homer Addams
S, E. Dibble, Vice-Chm, W. E. Gillham
F. Paul Anderson L, A. Harding
W. H, Carrier Alfred Kellogg
J. A. Cutler Thornton Lewis
William H. Driacoll Perry Wcat
H. P. Gant F. C. Houghten, Secy.
1921
President Champlain L, Riley
1st Vice~Pr«sident Jay R. McColl
Snd Vice-President H. P. Gant
Treasurer.^,,*,, „., » Homer Addams
Secretary. Casin W. Obert
1925
President .,, . S. 1C, Dibble
1st Vice-President. „. Wm. H. Driacoll
£nd Vice-President ...,R Paul Anderson
Treasurer. , , .„....,..„.....,.., /Perry West
Secretary.., .....F. C. Houghten
Council
Chairman, Champlain L, Riley
Jay R. McColl, Wct-Chm. E, S. Hallett
Homer Addams E. Vernon HU1
Joa. A. Cutler Alfred Kellogg
Samuel E. Dibble E. E. McNair
Wm. H* Driscoll Perry West
H. P, Gant Caste W. Obert, Secy.
Council
Chairman, S, E, Dibble
Wm* H. DriicoIl.PYce-CViw, W. T* Jones
Homer Addams Thornton Lewis
F, Paul Anderson J. H. Walker
W, H. Carrier Ferry West
T, A, Cutler A. C. Willmrd
W. E. GiJlham F. C. Houghten, .9,
, ...Jay R, McColl
Ut Vice-President^.., „..„.,....„ H, P, Gant
$nd Vi6*.J*rHident». ...Samuel E* Dibble
TY#asur$F ..................................... .„.„„. Homer Addama
Secretary Ctsin W. Obert
.,............«.» «,.,«....,.W. H* Driscoll
1st Vie*-Pr*ati&<tnt.~ ,,,,,F* Paul Anderson
SSnd Vfa-Prtsidtmt*^....*.- .,..A, C WIHwd
Treasurer, „„.„„„„...«... ...,.W« E, GHIham
.,...,...M.«...«...«..»..A. V.
Council
Chairman, Jay R. McColl
H, P, Gattt, Vice»Chm, L. A, Harding
Homer Addama E. E- McNair
Jos. A. Cutler H, J. Meyer
Samud E, Dibble C, JU Riley
Wm, H. 0ri8coll Perry West
E. S. Haitett Casin W. Obert, ,
Council
Chairman, W. H* Drfccoll
F. Paul Anderson, Vica»Chm* C> V. Hayne*
W. H. Carrier W. T. Jone«
J* A, Cutl«r E. B, Lutnaenber
S. E, Dibble Thomtoa Lewlt
W. E. Gillham J. F* I "
A, C, Wmard
ROLL OF MEMBERSHIP
1927
President F. Paul Anderson
1st Vice-President , A. C. Willard
8nd Vice-President Thornton Lewis
Treasurer W. E. Gillham
Secretary A. V. Hutchinson
Council
Chairman, F. Paul Anderson
A. C. Willard, Vice-Chm.
H. H. Angus
W. H. Carrier
W. H. Driscoll
Roswell Farnham
H. H. Fielding
W. E. Gillham
C. V. Haynes
John Howatt
W. T. Jones
J. J. Kissick
E. B. Langenberg
Thornton Lewis
J. F. Mclntire
H. Lee Moore
F. B. Rowley
1928
President A. C. Willard
1st Vice- President Thornton Lewis
8nd Vice-President L. A. Harding
Treasurer.^ W. E. Gillham
Secretary A. V. Hutchinson
Council
Chairman* A. C. WUlard
Thornton Lewis, Vice-Chm, C. V. Haynes
F. Paul Anderson John Howatt
H. H, Angus W, T. Jones
W, H. Carrier J. J. Kissick
E. B. 3
N. W. Downes
Langenberg
Roswell Farnham J. F. Mclntire
H, Lee
W. E. Gillham
F. B. Rowley
-ee Moore
1929
President,. ,. Thornton Lewis
1st Vicf- President. -.-L, A. Harding
$nd Vice-President.., .W, H, Carrier
Treasurer W. K. Gillham
Stcrttary' [.L.I......... .—A, V, Hutchinson
Technical Secretary.... ....,.,.— ............ P. D. Close
Council
Chairman, Thornton Lewis
L, A. Harding, Vice-Chm. John Howatt
H, H. An«ui w. T. Jones
W. H. Carrier K. B, Langenberg
N. W, Downee G. L. Larson
Roswell Farnham K. C. Mcintosh
W. E, Gillham W. A, Rowe
C. V, Haynes F. B, Rowley
A. C. Willard
1930
^,, .........
1st Vice-President ................ , .......
$nd Vice-President.^ _______ ........ .
..
Secretary „ ......
1931
President W. H. Carrier
1st Vice-President F. B. Rowley
2nd Vice- President W. T. Jones
Treasurer F. D. Mensing
Secretary _"..." "." ." A. V. Hutchinson
Technical Secretary P. D. Close
Council
Chairman, W. H.
F. B. Rowley, Vice-Chm.
D. S. Boyden
E. K. Campbell
R. H. Carpenter
J. D. Cassell
E. O. Eastwood
Roswell Farnham
E. H. Gurney
..t, A. Harding
-.W, H, Carrier
....F. B, Rowley
;••"•„• ,
..»..». ...... A. V. Hutchlnson
. ____ . ........... ,..,,«,.P. D. Close
Council
Chairman* L. A. Harding
W, H* Can-tor, Vte+Chm. John Howatt
H, H. Angua W* T. Jones
D, S. Boyden E. B, Langenberg
R, H. Carpenter G. L, Larson
J, D. Ca*s*ll Thornton Lewis
k W, Downs* F. C, Mclntosh
Rotwell Farnham W. A, &ow«
C, W, Farrar F, B. Rowley
Carrier
L. A. Harding
John Howatt
W. T. Jones
E. B. Langenberg
G. L. Larson
F. C. Mclntosh
F. D. Mensing
W. A. Rowe
1932
President F. B. Rowley
1st Vice-President W. T. Jones
&nd Vice-President C. V. Haynea
Treasurer.^ , » ....F. D. Mensing
Secretary A. V, Hutchinson
Technical Secretary P. D. Close
Council
Chairman, F. B. Rowley
W. T. Jones, Vice-Chm. F. E. Giesecke
D. S. Boyden E. Holt Gurney
E. 1C Campbell C. V. Haynes
R. H. Carpenter John Howatt
W. H. Carrier G. L. Larson
John D. Cassell J. F. Mclntire
E, 0. Eastwood F. D. Mensing
Roswell Farnham W. E. Stark
1933
President W. T. Jones
1st Vice-President.^.* ,C. V. Haynes
$nd Vice-president John Howatt
Treasurer..., D. S. Boyden
Secretary,.,., , A. V. Hutchinson
Council
Chairman, W. T. Jones
C. V, Haynea, Vice-Chm, G. L. Larson
R, H. Carpenter J. F. Mclntire
F. D. Caasell W. E. Stark
D. S. Boyden E. K. Campbell
John Howatt E. 0. Eastwood
k C. Mclntosh R. Farnham
L* W. Moon E, H, Gurney
F. E. Giesecke F. B. Rowley
1934
President , ..... ..C. V, Haynea
1st Vice-President ,... John Howatt
find Vict-President ........G. L, Larson
„„.,. „ ....D. S. Boyden
A. V. HutchinBon
Council
Chairman, C. V. Haynes
John Howatt, Vics-Chm. W, T\ Jones
M. C. Beman O. L. Larson
D S, Boyden J- F, Mclntire
Albert Buenger F. C. Mclntosh
R. H. Carpenter L. Walter Moon
LD, Cas«ell O. W, Ott
F, E. Gie«ecke W. A. Russell
E. H, Curney W. E, Stark
57
1 34 974