ML111960136
| ML111960136 | |
| Person / Time | |
|---|---|
| Site: | Crystal River  |
| Issue date: | 11/04/1981 |
| From: | Cross W Florida Power Corp |
| To: | Eisenhut D Office of Nuclear Reactor Regulation |
| Shared Package | |
| ML111960137 | List: |
| References | |
| 3F-1181-03, 3F-1181-3, NUDOCS 8111100419 | |
| Download: ML111960136 (56) | |
Text
-I 50-302 H. Pratt Coanalysis of REactor Building Purge Valves Rec'd w/ltr dtd 11-4-81 ACC.# 8111100419 RECORDS FACILITY BRANCH NOTICE THE ATTACHED FILES ARE OFFICIAL RECORDS OF THE DIVISION OF DOCUMENT CONTROL.
THEY HAVE BEEN CHARGED TO YOU FOR A LIMITED TIME PERIOD AND MUST BE RETURNED TO THE RECORDS FACILITY BRANCH 016.
PLEASE DO NOT SEND DOCUMENTS CHARGED OUT THROUGH THE MAIL. REMOVAL OF ANY PAGE(S) FROM DOCUMENT FOR REPRODUCTION MUST BE REFERRED TO FILE PERSONNEL.
DEADEflQf FH FOPY
/A
~
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CONTENTS Page I.
Introduction 1
Ii.
Considerations 2
III.
Method of Analysis 4
A.
Torque Calculation 6
B.
Valve Stress Analysis 7
C.
Operator Evaluation 8
IV.
Conclusion 9
V.
Additional Information 10 Attachments (1)
Input Documents (A)
Pressure v. Time Graph (B)
Pratt letter regarding additional information (C)
Customer/engineer response to request for information (2)
Valve Assembly Stress Report (3)
Operator Ratings (4)
Supplemental Torque Calculations (5)
General Arrangement and Cross-Section Drawings 9/
/6p&zf2&
I.
Introduction This investigation has been made in response to a request by the customer/engineer for evaluation of containment isolation/purge valves during a faulted condition arising from a loss of coolant accident (LOCA).
The analysis of the structural and operational adequacy of the valve assembly under such conditions is based principally upon containment pressure vs. time data, system response (delay) time, piping geometry upstream of the valve, back pressure due to ventilation components downstream of the valve, valve orientation and direction of valve closure.
The above data as furnished by the customer/engineer forms the basis for the analysis. Worst case conditions have been applied in the absence of definitive input.
2 II.
Considerations The NRC guidelines for demonstration of operability of purge and vent valves dated 9/27/79, have been incorporated in this evaluation as follows:
A.1. Valve closure time during a LOCA will be less than or equal to the no-flow time demonstrated during shop tests, since fluid dynamic effects tend to close a butterfly valve. Valve closure rate vs. time is based on a sinusoidal function.
- 2. Flow direction through valve contributing to highest torque; namely, flow toward the hub side of disc if asymmetric, is used in this analysis. Pressure on upstream side of valve as furnished by custcmer/engineer is utilized in calculations. Downstream pressure vs.
LOCA time is furnished by customer/engineer or assumed to be worst case.
- 3. Worst case is determined as a single valve closure of the inside containment valve, with the outside containment valve fixed at the fully open position.
- 4. Containment back pressure will have no effect on cylinder operation since the same back pressure will also be pre sent at the inlet side of the cylinder and differential pressure will be the same during operation.
- 5. Purge valves supplied by Henry Pratt Company do not normally include accumulators. Accumulators, when used, are for opening the valve rather than closing.
- 6. Torque limiting devices apply only to electric motor operators. Based on findings in this report, motor operator torque switches should be bypassed or re moved to eliminate motor lock-up during the LOCA closure cycle.
7&8.
Drawings or written description of valve orientation with respect to piping immediately upstream, as well as direction of valve closure, are furnished by customer/engineer.
In lieu of input, worst case conditions have been applied to the analysis; namely, 90o elbow (upstream) oriented 900 out-of-plane with respect to valve shaft, and leading edge of disc closing toward outer wall of elbow. Effects of downstream piping on system back pressure have been covered in paragraph A.2. (above).
B.
This analysis consists of a static analysis of the valve components indicating if the stress levels under combined seismic and LOCA conditions are less than 90% of yield strength of the materials used.
A valve operator evaluation is presented based on the operators ability to resist the reaction of LOCA-induced fluid dynamic torques.
C.
Sealing integrity can be evaluated as follows:
Decontamination chemicals have very little effect on EPT and stainless steel seats. Molded EPT seats are generically known to have a cumulative radiation resistance of 1 x 108 rads at a maximum incidence temperature of 350 0 F.
It is recommended that seats be visually inspected every 18 months and be replaced periodically as required.
Valves at outside ambient temperatures below O0 F, if not prop '
adjusted, may have leakage due to thermal contraction of the elastomer, however, during a LOCA, the valve internal temperature would be expected to be higher than ambient which tends to increase sealing capability after valve closure.
The presence of debris or damage to the seats would obviously impair sealing.
III.
Method of Analysis Determination of the structural and operational adequacy of the valve assembly is based on the calculation of LOCA-induced torque, valve stress analysis and operator evaluation.
A.
Torque calculation The torque of any open butterfly valve is the summation of fluid dynamic torque and bearing friction torque at any given disc angle.
Bearing friction torque is calculated from the following equation:
T B P x Ax U x d where P =pressure differential, psia A = projected disc area normal to flow, in 2 U = bearing coefficient of friction d = shaft diameter, in.
Fluid dynamic torque is calculated from the following equations:
For.subsonic flow
[R 1
1.07 (approx.)
P2 T
= D x CTI x P2 x x FRE D
TlE2 1.4:
For sonic flow P
R C
[
-RCR]
P 1 3
TD D
- 1)
- 1. 4 RE Where TD = fluid dynamic torque, in-lbs.
FRE = Reynold number factor RCR = critical pressure ratio, (f
(
)
)
p1
= upstream static pressure at flow condition, psia p 2
= downstream static pressure at flow condition, psia D
= disc diameter, in.
CTl = subsonic torque coefficient CT 2 = sonic torque coefficient K
= isentropic gas exponent (
1.2 for air/steam mix)
= disc angle, such that 900 = fully open; 00 = fully closed Note that CTl and CT 2 are a function of disc angle, an exponential function of pressure ratio, and are adjusted to a 5" test model using a function of Reynolds number.
Torque coefficients and exponential factors are derived from analysis of experimental test data and correlated with analytically predicted behavior of airfoils in compressible media.
Empirical and analytical findings confirm that subsonic and sonic flow conditions across the valve disc have an unequal and opposite effect on dynamic torque. Specifically, increases in up stream pressure in the subsonic range result in higher torque values, while increasing P1 in the sonic range results in lower torques.
Therefore, the point of greatest concern is the condition of initial sonic flow, which occurs at a critical pressure ratio.
The effect of valve closure during the transition from subsonic to sonic flow is to greatly amplify the resulting torques.
In fact, the maximum dynamic torque occurs when initial sonic flow occurs coincident with a disc angle of 720 (symmetric) or 680 (asymmetric) from the fully closed position.
D-29254-1 JOB: FLOP. PIR;CRYST. RIV P2-VARIABLE SIZE ADJSITED:REYNLD:
NO.FNCTN!)
SAT.STEAM-AIR MITURE WITH 1.4 LBS STEAM PER 1-LE:
AIR SPEC.GR.=.738255 MOL.WT.= 21.3872 KAPA(ISENT.EXP.)=
1.19775 GAS CONSTANT-CALC.
SONIC SPEED:MOVIN" MI:TR.)= 1316.65 FEET-SEC AT 225 DEG.
R= 72.1972 CRIT.CASE INLET VELOCITY IS 1.4606 TIMES HIGHER AS AIR CRIT.CASE INLET Mi-OF 5 INCH MODEL MAX.
TORQUE IS AT THE CRITICAL PRESS-.PATIO(.5 :35-:5 IN':MODEL OR APPX
.695051
( 47.375 IN)WITH STMIX.)FIRST SONIC ::@ 72 DEG.V.A.)
MAX.TOROUE INCLUDES SIZE EFFECT(REYNOLDS NO.ETC)APPX.
X 1.37246 FOR 47.375 INCH BASIC LINE I.D.
ALL PRESSURES UTSED: S TATICC"TAP)PRESS. -AB:OLUTE P2 INCL.RECOVERY PRESS.
(TORQUE) CALC.:
VALIDITY: P1.-P2> 1.07 VALVE TYPE:
DISC SIZE:
SHAFT DIA.:
BRG.
COEF.
OF FRCTN.:
SEATING FACTOR:
INLET PRESS.VAR. MA<.
OUTLET FEESTUEP:':
MA::. ANG. FLOSI RATE:
CRIT.SONIC FLOl.0-90DG:
VALVE INLET DENSITY:
FULL OPEN DELTA P:
48"-PR; 4 6.71 4.75 5.00IO00 15 5 0. 7 23.5 527196.
45093.9
- 6. 72714E 2416 176 INCHES INCHES 0 E -0C 3 CLASS 75 OFFSET ASYMMETRIC DISC PSIA PSIA (72 DEG.
ACTUAL PRESS.DONLY.:VAR.)::*:
CFM; 645142.
SCFM; 35465.2 LBEMIN LB/MIN AT 23.8381 INLET PSIA
-02 LBYFT^3-MIN.
.14:391 LE/FT^3-MAX.
PSI SYSTEM CONDITIONS::
PIPE IN-PIPE-OUT -AND-AIRSTEAM MIXTURE SERVICE 225 DEG.F MINIMUM 0.75 DIAM.
PIPE DOWNSTREAM FROM CENT.LINE SHAFT.
P1 ABS.
PRESSURE(ADJ..)FOLLOWS TIMEXPPESS.TRANSIENT CURVE.
ABSOLUTE MAX.TORUE IS DEPENDENT ON DELAY TIME AND 3.43 TO 2.15-TH POllER OF (P1-'P2)IN WORST RANGE :
LINEAR CONS:TANT
- DNTR.PRESS.
PE-AES. *:.75-6.DEG.:
IN SUBSONIC RANGE LIMITS-ONLY; SEE FORMULATIONS. -PER TETTS H.PRATT THIS TO.
AT 72 DEG.SYMM.
DISC
- 68=0FFSET SHAFT) CT=T/'D^3/-P2:ES)
ANGLE P1 APP::.P I 90 23.70 85 27. 28 80 30.07 75 32.51 72 33.81 70 34.61 65 36.:37 60 37.77 55 38.78 50 39.39 45 39.60 40 39.81 35 40.42 30 41.41 25 42.72 20 44.27 15 45.99 10 47.75 5
49.42 0 50.70
-- 5 IN.MODEL EQUIV. VALUES-------ACTUAL SIZE VALUES-P2 PT. IA 18.81
- 19. 45
- 20. 07 20.25 19.77
- 19. 64 1:.76 1
48 17.84 16.1-,
16.24 15.76 15.44
- 15. 12 14.93 14.82 14.76 14.71 14.71
- 14. 70 14.70 DELP PSI 4.8 7.-8
- 10. 0 12.2 14.0 14.9 17.6 19.9 21.'
23.1
- 23. E 24.3 25.:
26.4 27.8 29.5 31.2 33.0 34.7 36.0 PRESS.
FLOI FLOil RATIO
- SCFM)
(LB'MIN) 9
.794 645141
- 35465 3
.713 737320 40532 0
.667 783456 43068 6
.623 806358 44327 4
.59.5 CRp 767504 42191 7
.567 CR 74:3916 41169 1
516 CR 69 009?0 37936 2
.472 601228 33051
- 9
.435 511847 2813r' 5
.412 421302 23160
- 4
.398 418401 23000
?6
. :-:- 3 294358 16181 0
.374 222007 122'4 8
.361 168176 9245 9
.347 120845 6643 1
.333 75650 4158 8
.320 43501 2391 5
.303 22153 1217 2
.297 7269 399 0
.290 0
0 TD TB+TH I NCHLS----
TD 596E6:-:
120605 171107 323497 465275 434405 336144 293011 217958 190308 1426 12 96397 59081 41362 31029 11965 6409 4290 34398 111 430 455 41 1
270 24 C
295 327 354 384 433 496 687 781 7:32 TIME':LOCA.
-TE-TH SEC.
59 608 1.00 120494 1.43 0170949 1.@36 323198 2.25 4e4 45 2.47 4 37 9 5:3 2.61 434003 2.92
- 33583:
- 3. 17 292741 3.35 217693 3.46 190012 3.50 1422:
4
.54 96 043:
3.65 58696
- 3. 83 40921
-4. 0 -S 30533 4.29 113:1 4.75 5721 5.14 3508
- 5.
57 3366'5
- 6. 0' SEATING + BEARING
+ HUE SEAL TOROUE (MM:*=
- 34398 IN-LES 0 DEG.
MAX. DYN.
BEARING HUB SEAL TORQUE
- M'M*
=
465275 IN-LS 70 DEG.
f A
/
7 B.
Valve Stress Analysis The Pratt butterfly valve furnished was specifically designed for the requirements of the original order which did not include specific LOCA conditions.
The valve stress analysis consists of two major sections:
- 1) the body analysis, and 2) all other components.
The body is analyzed per rules and equations given in paragraph NB 3545 of Section III of the ASME Boiler and Pressure Vessel Code.
The other components are analyzed per a basic strength of materials type of approach. For each component of interest, tensile and shear stress levels are calculated. They are then combined using the
.formula:
Smax =
l2 jT 1
2 )2 + 4(S+S2) 2 2
where Smax = maximum combined stress, psi T1
= direct tensile stress, psi T2
= tensile stress due to bending, psi Sl
= direct shear stress, psi S2
= shear stress due to torsion, psi The calculated maximum valve torque resulting from LOCA conditions is used in the seismic stress analysis, attachment #2, along with "G" loads per design specification. The calculated stress values are compared to code allowables if possible, or LOCA allowables of 90%
of the yield strength of the material used.
8 C.
Operator'Analysis This analysis specifically evaluates the worst case, inside containment, valve with Li/mitorque operator.
The rating of the outside Bettis operated valve is included for informational purposes only.
Model:
Limitorque SMB 1-40/H3BC Rating:
67800 in-lbs.
Max. Valve Torque:
465275 in-lbs.
Model:
Bettis T520-SR2 Rating:
225,000 in-lbs. (at full open and closed positions only)
The operators furnished were specifically designed for the requirements of the original order which did not include specific LOCA conditions.
The maximum torque generated during a LOCA induces reactive forces in the load carrying components of the actuator.
The Limitorque model furnished has a rating which ex ceeds the calculated valve torque for the following valve angles:
40 degrees open to 0 degrees (fully closed)
The Bettis model furnished has a rating which exceeds the calculated valve torque for the following valve angles:
55 degrees open to 0 degrees (fully closed)
Listed in the attachments section of this report are the following documents used in evaluating the structural and operational adequacy of the actuators.
-Operator Rating (Attachment #3)
-Supplemental Torque Calculations (Attachment #4)
9 IV.
Conclusidns It is concluded that neither the valve structure (with present materials) nor the valve actuator are adequate to withstand the defined LOCA-induced loads based on the calculated torques developed in this analysis except for restricted valve opening as described below:
Specifically, the valve top stub shaft and top disc hub blocks are shown to be overstressed except at valve disc angles of 600 or less (see attachments 2 and 4).
In addition, the calculated torques exceed the manufacturers rating for the actuator except at valve disc angles of 400 or less (Limitorque Operator) and 55 or less (Bettis Operator).
(See attachments 3 and 4)
V.
Additional Information The following items are presented to describe how system factors affect torques developed in this analysis for your consideration and are informational only.
Further analysis by the customer/engineer is recommended prior to implementation.
- 1.
An important factor governing the magnitude of the dynamic torque is delay time from the start of a LOCA incident to activation of the pressure sensing mechanism, which in turn initiates valve closure. Careful re-evaluation by the customer/engineer of the pressure sensing/timing sequence may render the present valve assembly functional through a significantly greater range of angles.
- 2.
Installation of a convergent-divergent section downstream of the outside containment valve with a throat area sufficient to allow unrestricted ventilation during normal operation, but which will choke LOCA-induced flow while the valve is closing, through the critical range of 800-600 open, could resultantly reduce the flow through the valve to subsonic levels.
- 3.
An orifice plate installed similar to #2 above can also choke the system downstream and reduce flow through the valve to subsonic levels.
- 4.
Mechanically restrict or block the valve disc to a maximum disc opening angle.
(See attachment #4 for further illustration).
ATTACHMENT lA PRESSURE vs.
TIME GRAPHS
70 60 50 40 30 20 10 0 10 102 103 Time After Rupture. s REACTOR BUILDING PRESSURE VERSUS TIME FOR 14.1 FT 2 HOT LEG BREAK CRYSTAL RIVER UNIT 3 FIGURE 14-72B coflo~ArO (AM. 27 6-29-73)
70 50 40 30 20 110-1 100 101 102 103 Time After Rupture, s REACTOR BUILDING PRESSURE
-VERSUS TIME FOR 11.0 FT2 HOT LEG BREAK
-CRYSTAL RIVER UNIT 3
=7" FIGURE 14-72C (AM.
27 6-29-73)
760 TH I*
I I
50 40 3o 20 10 3
40 10.1 100 101 102 103 Time After Rupture, s REACTOR BUILDING PRESSURE VERSUS TIME FOR 8.55 FT' HOT LEG BREAK CRYSTAL RIVER UNIT 3
- FIGURE 14-72D cora~.(A M. 27 6-29-7 3)
70 80 50 40 30 20
~~
3D 2210 10 0
101 10 10-1 10 Time After Rupture. s REACTOR BUILDING PRESSURE YERSUS TIME FOR 5.0 FT 2 HOT LEG BREAK CRYSTAL RIVER UNIT 3 FIGURE 14-72E coCo-MtoW (AM. 27 6-29-73)
ATTACHMENT lB PRATT LETTER REGARDING ADDITIONAL INFORMATION
PRATT HENRY PIRALT COMP IANY
)01 S l11 IllGilLAND AVICNti ALItltA. IIJ.N IS (K)5(7 December 3, 1980 Florida Power and Light Co.
P.O. Box 14042 St. Petersburg, FL 33733 Attention:
Mr. K.M. Elder Project Engineer
Subject:
Crystal River -
Unit #3 48" Purge Valve Analysis A-49210Q
Dear Mr. Elder:
Recent findings in the general analysis of purge valves sub jected to LOCA conditions have necessitated a request for additional technical data from the customer/engineer.
Delay time, system back pressure and valve orientation have a significant impact upon maximum torque and resultant stresses in the valve assembly. To properly complete the purge valve analysis referenced above, the following information is re quired:
- 1. The combined resistance coefficient for all ventilation system components downstream of the valve (one for each valve size)or A graph of back pressure vs. LOCA time at a distance 10-12 diameters dIownstream of the valve.
Consider also he capacity of the piping, filter and duct work to resist increases in back pressure.
- 2.
Maximum and minimum delay times from LOCA to initiation of valve rotation.
mstcd
PRATT Mr. Elder Page 2 December 3, 1980
- 3.
Drawings or written description of valve orientation with respect to elbow immediately upstream of valve (within 6 diameters), as well as direction of valve closure (clock wise or counterclockwise) as viewed from operator end.
In the absence of the above information, the following assump tions will apply to the purge valve analysis;
- 1.
Back pressure of 19.7 psia throughout valve closing cycle. ?
Higher back pressure increases maximum dynamic torque and valve stresses.
- 2.
Delay time from LOCA to initiation of valve rotation shall be chosen to permit initial sonic flow condition and critical valve disc angle to coincide, resulting in maximum possible dynamic torque.
- 3.
900 elbow immediately upstream, oriented 900 out-of-plane with respect to valve shaft, with leading edge of disc closing away from outside radius of elbow. Such orien tation and closure will increase torque.values by 20% or more.
Your prompt response within 30 days would be appreciated.
Very truly yours, HENRY PRATT COMPANY T.J. Wrona, Manager Contract and Proposal Engineering
/sW CC:
R.D. Nelson
~~msted
ATTACHMENT IC CUSTOMER/ENGINEER RESPONSE TO REQUEST FOR INFORMATION
Florida Power February 4, 1981 CORPORATION Henry Pratt Company 401 S. Highland Avenue Aurora, IL 60507 Attention: Mr. T. J. Wrona
Subject:
Crystal River Unit #3 48" Purge Valve Analysis (AHV-1A,B,C,D)
FPC P.O. No. A-49210Q
Reference:
Henry Pratt Company ltr. Wrona to Elder dtd Dec. 3, 1980
Dear Yr. Wrona:
In accordance with your request for additional information per the referenced letter, and our telephone conversation of February 2, please find the attached drawings which depict the arrangement of ductwork and components associated with the subject valves.
Hopefully this will provide enough data for Pratt to calculate the required resistance coefficients necessary for the analysis.
Also, please find the attached graphs taken from CR-31s FEAR depicting Reactor Building pressure versus time following various LOCA break sizes.
Actuation of the valves will take place after the Reactor Building pressure reaches A psig (about 0.5 to 1 second depending upon break size.).
In addition, there will be a delay of approximately 0.5 second for the ES signal to reach the actuator.
(Reference B&W ltr FPC-80-016 dtd 6/30/80 and CAI ltr.
FCS-1442 dtd 1/8/81.)
The orientation of the valves and the direction of closure is shown on the attached Pratt drawing.
It is understood that this analysis can be completed 30 days after receipt of this information, provided it is sufficient.
If further delays are anticipated or if the information which we are sending you is insufficient, please contact me immediately at (813) 866-4419. Thank you for your assistance.
Sincerely, A POWER CORPORATION G.A. Becker Supervisor, Mech./Struct. Engineering GAB/jw enclosure cc: E.C. Simpson P.Y. Baynard T.C. Lutkehaus F.J. Tomazic (CAI)
Readers File: EQ 3-5-31 w/attach General Office 3201 Thirty-fourth Street South e P.O Box 14042. St. Petersburg, Florida 33733
- 813-866-5151
REACTOR BUILDIbIg 5 HAF SIDe (Bettis spring opposed air operated)
RE P.i I
0 HUB LOC.K S HA.PT GID 6 (Limitorque Operators)
Valve AHV-1A & lB have operator met..c- -a dt=
MACHINING TOLERANCES I
U"its5 0Itl(
RVISE SP(CIf It D.
IAAC TIONAI QsM Nes,04%
1t4
.LCSMAL L-
.Mt hd
.OS 0 IlL AN(.
LES 10 L.at1 TLNS' ON COMMON CINEERLINL ARE T0 BE CONCtNIRIC llH.
14 0 T.1 N.R A
AAI.
SUl t
MOUHNFSS R
M 5.
All IIItNS ANI*
4 I At At I I4ARP CORNERS 9 HNRY PRATT COMPANY qwv,,^\\,
VE IL1.A'
^,,,t,
_A
% -1 MATFRIAL SPECIFICATION'.; ~
FrEV. O.)
/5 TF DY APP.
REV. DATE Y
APP.
V --
V -
C) rt tot(N BY :iC-. %
CKIIi BY I
AT T7A/AVE/V T F~c~
A~Dy~~
~(*~
5-7, 2
4
/
e SEISMIC ANALYSIS for 48 inch Nuclear Purge Valve a
A
Prepared by
(
914 2-Approved by
.7,;--'
PROJECT -
Gilbert Associates - Florida Power Corp.
PRATT ORDER NO.
7-3915 CUSTOMER ORDER NO.
PR3-1783 Q VALVE SIZE 48 inch SEISMIC ACCELERATIONS 5 9's simultaneously applied in each of three perpendicular directions.
Summarized in the following two tables are the stress intensities of primary concern. Table I identifies body stresses nnd how they re lte to the "Draft ASHE Code for Pumps and Valves for Nuclear mower" dated Nov., 1968.
Table 11 identifies stresses in other elcments of the butterfly valve assembly, for which the pump and valve code pro video no specific analysis procedure. All allowable stress levels are as specified in Table A-1 of the code.
TABLE I -
Body Stress Levels Stress Name Primary Membrane Stress In sity Primary & Secondary Stresses 4ue to flange, pressure, and
- V etsmic loads.
Secondary Stresses Due to Pipe Reaction Valve Body Secondary Stresses Fatigue Stress (Na2 2,000)
Code Ref.
Par.
452.3 452.4a Code Sym.
Qp Analysis Ref.
Pg.
Stress Level 5
1,025 5
5,177 452.4b 452.4 452.5 Ped Peb Pet Sn sp 6
7 7
3,317 6,896 555 12,165 8,967 Allowable Stress Sm 18,900 1.5 Sm 28,350
- 1. 5 Sm 28,350 6,00 65,000 Notes: 1.
Body material is carbon steel per ASTM A-516, Gr. 60.
- 2. Allowable stresses are for 3000 F.
- 3.
Valve Tag No.'s are: ARV 1A ARV lB AHV lC ARV 1D
/
/
Prepared by j?~-~-~~ t2~-~v-7c'
11I
- pnn-rod~ fned Stron Levels 7 1ve Coipflonent Dis~c Shaft Shnft Retainer Accembly Hub Block AsseLmbly Thrust Bearing Asserbly Stress Mtaximum Dice Streess Maximum Shaft Strees Retainer Shear Strens Retainer Bearing Stress Dolt Tensile es Stcrflss l
Shaft Groove Shear Stress Key-tiy Bearing Stresns max. Combined Bolt Stress T. Washer Normal T.Uner Seismic BeAring Stress Adjusting Screw ShenrSrs Adjusting Screw Tensile Stress Retalning Screw Tensile Stress Cover Shear Stress Analynis
- jterlial Streno Ref.
Pg.
LevelA ASTI A-516 8
Gr.
60 8,064 ASTM4 A-479 Type 304 38,937 ASTM A-240 10 Type 304 6,500 10 ASTI-I A-240
-0 10 11 11 13 13 13 13 13 13 ASTIA A-540 CL.1,Gr.B2' AsTH A-479 Type 304 ASTIM A-350 Gr.LF-1 ASTM A-540 CL.1,Gr.B2:
13,200 38,700 3,400 60,870 38,640 Slcn L Brouze415 Silicon Lub Bronze 2 075 ASTI A-479 Type 316 6,150 ATH A-479 Type 316 11,200 ASTM A-540 CL.1,Gr.B21 21,100
'iTIM A-285 Gr.C 2,300 I
8,000
.5 Sca 20,000 SM 46,200 8,85
- Not specified in pump and valve code.
Note:
Allowable stresses are for 3000 F.
A1101eb'13le Stress 18,900
- 9Sy =
27,000
.5 S'a 9,900 Sm 19, P)0 Sm 46 200
.5 S--i 9,900
.9 Sy 27,000 S
SI 46,200 11 I
% 1 1
NUCLEAR PURGE VALVE STRESS ANALYSIS T
Prepared by Approved by INTRODUCTION Described briefly in the following pages is the analysis used in verifying the structural adequacy oi the main elements of the butter fly valve.
E~ach element is described separately in its own, appropri ately titled, section.
Seismic loads were made an integral part of this analysis by the inclusion of the acceleration constants gXI. gyp 9., Should they not be present in any of the directions of interest, simply set the appropriate value of gi to zero.
The symbols x g, oiand g represent accelerations in the x, y, and z directions respectively. These directions are defined with respect to the valve body centered coordinate system illustrated in the figure 1.
Specifically x is along the pipe axis. z is along the shaft axis.
y is perpendicular to x & y and in the direction forming a right hand triad with them.
Valve orientation with respect to gravity is taken into account by adding the appropriate quantity to the seismic loads.
The justification for doing this is that a gravitational load is completely equivalent to a 1 "g" seismic load.
As an example of including gravitational loads, consider a valve
. J oriented so that z is vertical and subjected to seismic loads GX9 GY9 and G.
The appropriate valves for g. gy, and g. would be:
g,9=G gy G y 9z 1 + Gz Throughout the analysis, reference is made to a "banjo" assembly.
This is the assembly consisting of the disc, the stub shafts, the hub blocks, and the mounting hardware.
It is termed a "banjo" assembly sim ply because it resembles a banjo in appearance, and this is an easy way to refer to it.
The main elements of the bnjo assembly are identified in figure 2.
Page 1 Of I-
F Tlvilr 1 -
VALVE 7109Y CENTERET) rO-ORDTR1TE SYSTEM FOR DEFTNINr, ACCELERATION DIREC (T Iorl
,/
I (he Y
/
Pa"'2 Of 1
IF HENRY PRATT CO.
AURORA. ILL.
I'
'~*
?
evtPACO DArE I
-HUB BL-,
REYWAN ONj
_6KE. OF 'OPRut e)LOCK4 ON.
A.
/
/
/
/
~ET~1N~~
e6oLT5 SHAFT g5.TAlaERS BCMOoM LtUS SHAT r
Page 3 of 14
'A-F re 2 -
Essential Features Ou Itanjo Assembly I
REFERENCE NO.
FILE NO.
-a o.
Y TOP TUe SHA--T
Prepared by.
o Approved by FLANGE ANALYSIS The flange nnalyiis is in accordance with Appendix II, Parn. VA-56 of Section VIII, Division I, of the ASME Codes for Pressure Vessels and AWWA C-207.
Page 4 Of I
Approved by BODY ANALYSIS With one excptio, the body analysis is in accordance with "Draft ASME Code for Pumps ::nc VaLvts o r Nucl c
r Pow r" dated Nov., econd exceptiOL is-in tie calculati-n of valve body primary pius secondary stress due to internal pressure, a quantity labeled as Q in section 452.4a of the code.
The formula which is specified in tnis section and considers only stresses induced by internal pressure is not used.
In its place has been substituted a more complete formulation which considers stresses induced by internal pressure, flange moments, and seismic loads.
All other body strss calculations are exactly per the pump and valve code.
The specific formulas used in calculating the body stresses are listed below.
- 1. Primary membrane stress - The following formula which satisfies the intent of.section 452.36 of the code was used.
Pn -
(Rm/h + 1/2) p where:
Rm = shell mean radius-inches p = internal pressure-psig h -
shell thickness-inches
- 2. Valve body primary plus secondary stresses due to internal pressure, flange moTrents, and inertial loads -
This is the quantity which re places Qp as defined in section 452.4a of the code.
It is calculated for two sections on the valve body, the section where the flange joins the body, and the section defined by the centerline of the valve shaft.
The largest of these two valves is then taken as Qp. The formula used for calculating Qp is:
Qp = 1/2 P + 1/2 (Qpl + Qp2) + 1/2 V(Qpl - Qp2) 2 + 4 y 2 where:
Y -
sum of shear stresses due to inertia torques and inertia transverse shear.-psi Qpl axial stresses-psi Qp2 - circumferential stresses-psi P -
internal pressure-psig The quantities Y, Q.1, and Qp2 are calculated from the following for mulas:
y. 2WRo
[Ec ex + L (p 2 + Fz2)1/2 77(Ro -R 4 )
(
+ 2 1/2 QPl = PRm/2h + 6M/h 2 + 77
_Ko R 1 p2.
PRn/h + 6(M/h2-wE/Rm Page 5 Of I'
Prepared y Approved by where:
P -
internal pressure-psig W
valve jeight-pounds Ro = outside radLus of valve body-inches Ri w inside radius of valve body-inches L = valve length-inches Ec - valve body eccentivityinches Rm = mean radius of valve body-inches h = valve body thickness-inches E = young's modulus-psi PV= poisson's ratio X9
= acceleration constants V %efection of valve body-inches X xg local bending moment per unit circumference-pounds Note:
W and M are calculated in a separate analysis, the details of which are not included here.
- 3. Secondany stresses due to pipe reaction-These are calculated using the equations of section 452.46 of the Pump and Valve code.
More speci fically, these are:
FdS Ped = d Peb C F S GUb Pet =2FS G
where:
Ped = direct, or axial, load effect-psi Peb = bending load effect-psi Pet = torsional load effect-psi
. P bending moduluS of standard connected pipe per figures 452.4b of pump and valve code-inches Yd -
1/2 the cross sectional area of standard connected pipe inches Cb-stress index for body bending secondary stress per section 452.4b S
30,000 per section 452.4b 2
Gd
=valve body section area-inches Gt
=valve body section torsional modulus-iches 3
Gb =valve body section bending modulus-ili~cs 3
- 4.
Thermal Secondary Stress-This stress is calculated per section 452.4ce of the Pump and Valve code.
More specifically, the formulas used were:
QT -
17.5 h2 for austenetic steel QT -
50.0 h2 for ferritic steel where:
QT = thermal secondary stress h -
thickness of valve body
/
Page 6 Of I.
Prepared by Approved by
- 5.
Combined Stress Intensity-Tis ciuantity, as specified -in section 452.4 of the Pump and Valve code is given by the formula:
Sn = Qp + Pe + 2QT where:
Sn = combined stress intensity Qp is given under number. 2, above.
QT is given under number 4, above.
Pe is the largest of Ped, Peb, Pet as given in number 3, above.
- 6.
Fatiguie Stresses-The valte taken for comparison with figures 452.5 (a) and 452.5 (b) of the Pump and Valve code is the larger of the following, as given in section 452.5:
Spl - 2Qp/3 + Peb/2 + 1.3 QT Sp2 =
4 P + Peb where all terms are as previously defined P
Page 7 Of IA
Approved DISC ANALYST!;
For an air purge valve, te worst load combination which occurs is combined pressure pliiS seisic loads.
The highest ma~gnitu~de stresses are peeta the center of the disc and can be considered as being the result of simnul taneous bending about two perpendicular axes, tie y axis and the z axis.
The magnitude of thle stress is given by:
(P + Pe) d [36 (.125 91a +.113d)2 1/2 Where:
Pe =
equivalent seismic pressure wtgx -
psi w
weight density of disc -
Pd/in3 t
thickness.of disc -
inches gx.
acceleration constant p
applied pressure - psig d
diameter of disc -
inches a
= unsupported shaft length -
inches it usually occurs that disc thickness is dictated by deflection requirements and that disc stresses are well below code a.lowable levels.
Page 8 of 14
Prepared by Approved by i'ta SHAFT ANALYSIS Because of the manner in which the purge valve isusd, fluid dy namic loadings can be negocCtcd.
Therefore, the worst loading condition on the shaft will be either a combination of torsional plus seismic loads or a combination of pressure plus seismic loads. loth of these condi tions were checked using the formulas listed below.
Columnar tensile and compsessive loads on the shaft were not considered because of their ob viously small effect on stress levels.
- 1.
Shaft Stress due to torsion plus seismic loads.
OE'-0 +- J T2+4Y 1/2 2
B 2LBTY.
TI where: c bending stress
=
2d 2)1/2a 04 torsional stress 16S02 7 d3 W = weight of banjo assy. -
Pds.
a = unsupported shaft length -
inches D = disc diameter -
inches S = seating factor -
Pds/inch d = shaft diameter inches gx99 y=
acceleration constants
- 2.
Shaft Stresses due to pressure plus seismic loads. - Both shear and bending stresses are calculated. However, they are not combined since their maxima occur at different locations on the cross section.
[K(77D2P/4 +
+g)2 (Wgy)2 1/2 OB-
[x 2 + o 23 1/2 where:
0 L(.125 7D 2P +.5 wgx)a 77d A = cross sectional area of shaft -
in2 P = applied pressure - psig D = disc diameter -
inches d = shaft diameter -
inches*
W = weight of banijo -
pounds a = unsupported shaft length -
inches gxPy =acceleration constants Page 9 Of 14
Approved by
/
- /
SIAFT RETAIN;it A;SaULY For purposes of convenience in description, the shaft retainer assembly is considered to consit of the sliftb retiner, the shaft re taincr bolts, and the grouved end of the. stub shaft.
The :-hoift retniner was checke'd foi: shear tear out aiid bearing~ stresses.
The shaft retainer bolts were checked for tensile stresses 3~SRining all four retainer bolts to be equally loaded.
Thc grooved end of the shaft was checked for shear tear out and bcnring stress.
Formulas for calculating each of these stresses are listed below.
- 1. Shear stress in retainer Or
=2Wez 77dt
- 2. Bearing stress on retainer and groove OB~ =.iM zg.
77 (
dr2
- 3. Tensile stress in retainer bolts y -
Wg 7
- 4. Shear tear out of shaft groove ass
- 2ri 77drL where: W = weight of banjo -
pounds d = shaft diameter -
inches dr = diameter of retainer bore -
inches t -
shaft retainer thickness -
inches A -
tensile area of retainer bolts -
in 2 L -
length of shaft after groove -
inches gz acceleration constant Pe 10 Of 14
Approved by..
(
,/
Illn BLtX'K ASWSEMBLY The hub block assembly is considered to consist of the hub block, the hub block retaining boLLs, aid the huh block keyway.
The two stresses of primary concern in the hu) block assembly are the keyway stresses and the combined tensile plus shear stresses in the hub block bolts. The analysis of each of these is explained below.
- 1. Hub Block Keyway -
The hub block keyway can be safely designed by keeping the compressive bearing stress on the keyway face below the allowable stress lcvel for the hub block material. The bear ing stress is calculated using the following formula:
on 4_
dKL where:
d = shaft diameter -
inches K -
key height -
inches L = key length -
inches rrh<= MAX/, DYNMAC IfDhau-4!GQ2
- 2. Hub Block Bolt Stress -
The hub block bolts are sized and located such that the maximum combined shear plus tensile stress does not exceed the code allowable value for the bolting material. Stresses are combined in accordance with the formula:
0 = [0I2 + 4-s 1/2 where: 0= combined stress level Ot = tensile stress Os = shear stress The value for Os is obtained by evaluating the following formula:
Wgz 3A where:
W = banjo weight -
pounds A -
tensile area of bolt -
in" gs M acceleration constant The value for O is obtained by evaluating the formula given below.
..This formula is the result of an analysis which considers the effect or pressure plus seismic loads in the x direction, moment from these loads in the x direction re:;ulting from unsupported shaft length, and moment and wedging effects from loads in the Y direction.
Page 11 Of 14
Prepared by It-LL
/
Approved by 0i- =
7C
- y.
(A +
)
wgy
+ AL
~1B
+ Ynx;
+
22A2_
2' C -_J 6
2(A2 2+C2 12A 3
1 F 2
where: At = bolt tensile area -
in D = disc diameter -
inches P = applied pressure -
pstg W = banjo weight -
pounds gx~y - acceleration constants A - distance from hub edge to first bolt pain -
inches B = distance from hub edge to second bolt pain -
incites C = distance from hub edge to third bolt pain -
inches d -
shaft diameter -
inches a
- unsupported shaft length - inches R -
distance between bolt rows -
inches Page 12 Of I-
Prepared by
. V-..-
)
Approved by, C..
THRUST BEARING ASSEMBLY The thrust bearing assembly provides restraint in the z direction for the banjo assembly, this assuring the disc edge remnins correctly positioned to maintain sealing capability.
Structural adequacy of the assembly was checked using the six formulas listed below. Specific elements of the thrust bearing as referred to below are identified in figure 3.
- 1.
Normal bearing stress on thrust washer.
Al
- 2.
Seismic bearing stress on thrust washer.
Ai
- 3. Shear stress in adjusting screw head.
Osn "Ez' 77Dt
- 4. Tensile stress in adjusting screw.
to=
gzW
- 5.
Shear stresses in cover.
.9 77DT
- 6.
Tensile stress in retaining screws.
Otr -gzW A3 vhere:
W = banjo weight -
pounds 2
A =-bearing area of thrust washer -
in SE = acceleration constant D - diameter of adjusting screw -
inches t -
thickness of adijusting screw head -
inches A2 tensile oare of adjusting screw -
in.2 T -
cover thickness -
inches 2
A3
= tensile area of retaining screws -
in.
Page 13 Of I-
U HENRY PRATT CO.
AURORA. ILL.
tIM PAI4LO UAT CHI CK0, V1A rkC Pre 3 -
Essential Features Of Thrust Bearing Ai;scmbly REFERENCE NO.
FILE NO.
VALVE B cOY Page 14 Of 1A 1
I j
/
ATTACHMENT 3
OPERATOR RATINGS
L A a I U 3MU V7.A L VEaC T L 2 ML %vS K
-~
~-.
p~,Ijt
'j~.7I7-~ -
.~
ii)
Butterfly Valve manual operator size H3BC.
A>.
I Motorized Limitorque Valve Control type SMB with H4BC manual.
I The hand operated type H-BC unit is a worm gear drive which may be used for any valve or device requiring a 900 movement. The H-BC manual gear operator is especially designed for operation of butterfly. plug and ball valves.
Every H-BC operator has an adjustable mechanical stop limit device to prevent movement of the valve beyond 90' of travel. Instructions for setting these limit stops are described elsewhere in this bulletin.
The manual H-BC operator has an alloy steel worm shaft and a bronze worm gear. On all units, except for buried service, a valve position pointer is furnished as a standard kiepart of the operator. On buried and submersible units.
stainless steel non-corrosive input shafts are furnished.
Handwheels are optional and can be furnished in various sizes as an extra.
All units are built to meet the requirements of A.W.W.A.
specifications and when spur gear or bevel gear attachments are used, the maximum input torque is less than 80 ft.
pounds to develop the maximum output torque rating of the unit with standard or optional gear ratios.
All sizes of units can be furnished with Linitoiue vqale controls or can be readily converted for motor operation in the field using Limitorque valve controls. The speed of operation of butterfly, plug or ball valves, when motor operated, is usually 20 to 30 seconds, however this can be varied over a wide range limited only by motor speed and available gear ratios.
- A PRODUCT OF LIfViTORGUE CORPORATION m C
Z 01 IVIANUAL TYPE HBC
INFORIATIOl IEEDED FOR ORDER To size a manual operator, we need:
- 1. -
Torque at valve shaft.
- 2. -
Valve shaft and keyway size.
- 3. -
Degrees of travel. *
- 4. -
Type of enclosure. weatherproof. buried or submersible. (If submersible. describe depth and time)
- 5. -
Position of assembly.
For motor operation, in addition to 1he above, we need:
- 6. -
Operating times.
- 7. -
Voltage. phase and cycles (or DC volts).
- 8. -
Type and frequency of service.
- 9. -
Maximum ambient temperature.
10.-
Class
- desired, weatherproof, explosion proof, or submersible.
I 1. -
Type of motor starter enclosure.
- 12. -
Type of pushbutton station enclosure.
a-.
SELECTION CHART FOR MANUAL OPERATORS UNIT SIZE OUTPUT TORQUE RATING WORM GEAR SPUR OR BEVEL GEAR TOTAL H.W. TURNS FOR 900 INCH POUNDS FT. POUNDS RATIO ATTACHMENT RATIO WITH ATTACH.
SPUR OR BEVEL HOBC 5,340 445 71:1 1:1 (bevel only) 17.7 H1BC 15,600 1,300 70:1 2.86:1 50 H2BC 26,400 2,200 70:1 2.86:1 50 H3BC 67,800 5,650 70:1 2.86:1 50 H4BC 153,600 12,800 60:1 12.0:1 180 H5BC 235,000 19,583 65:1 12.0:1 195 H6BC 552,000 46,000 66:1 38.9:1 641.8 H7BC 760,000 63,333 69:1 38.9:1 671
- ALTERNATE OPTIONAL RATIOS AVAILABLE ON REQUEST.
HOBC-H7BC STANDARD WEATHERPROOF UNIT POS "A" FOR INSTALLATION PURPOSES USE CERTIFIED DIMENSIONS ONLY.
UNIT SIZE A
B C
D E
F G
H J
K L
M N
0 P
R INPUT SH4AFT SPLINES S
T H B 2 4 7V.
1%
I 2As 6 0, 3
1 8 194 x
3 1/4
-13 8
3A 15T. INV. SPL.
%> D.P 16x/ 9 14 H I-bC 31 b'/,
- 87.
2 1
- 8.
3,1 1
[
1 10 11 88 H ?-BC
- 4.
5'16 9
I ]
2" 3"
I" 11i i?"u I10 5
1 o 1R0 -.3 1?5 WI DL j.
12!
3B 6
7%,
10
?
1,4 1 "A.9 4,/
1 3
14 1C e,16 10 8
6 H 4 -B C 7 !
9 b
13 i 3
1 %
3 10 4
1 1I l
I 1 0-It7 F5 3
W I D E 1 N IbS 1
H B5-C 9,A 103/L 14 3
1 3'.
110 5
I" 1
64 "t. 21 1
1r 8 1ir-10 I 5.':,
11.4 46 WIDE 13 13 t 18%
4 2.415 4V:
131".
6,/
1i 71/7 23
' b6 1 1.I'/0,
V. 7 8
10 I r 1N I I iI
?
53 PD 13 H
_7 C
1 15V 19 4
21 5
14, 6
2 7,
29 31,f ]%x)
>8/, 1.-
8 8
.W.
L.
13x) 2 NOTE: FOR SIZE H-7-BC WITHOUT SPLINED ADAPTER MAXIMUM BORE IS 84" WITH 2"x12" KEY.
Copyright (, Limitorque Corpora
7031GrandBlvd.
P.O Box 14689 Houston.Texas 77021 I
&13)748-1143 Telex76-2713 A Galveston -Houston Company January 15, 1981 Henry Pratt Company 401 South Highland Ave.
Aurora, Illinois 60507 Attention:
Mr. Ted Wrona
Subject:
T-5 Actuator Yoke Assembly Torque Absorbing Capabilities
Dear Mr. Wrona:
This is in response to our telephone conversation of Janu ary 12, 1981 concerning the torque absorbing capabilities of T-5 actuators; specifically a Model T516B-SR3.
Attached is a typical set of data for a Model T-520B double acting actuator.
Please note that the yoke assembly mecha nism for both double acting and spring return actuators is identical.
Consequently, the torque absorbing capabiltiy of a spring return actuator is the same as a double acting unit (i.e., 225,000 lb-in at either the full open or full closed (0-900) positions).
From the graph or tabulated data the per centage of torque outputs at 150 and 750 positions with respect to 00 and 900 torques is 74.5 and 72.6 percent each, respective ly.
Based on this, the yoke assembly (rated at 225,000 lb-in) should be capable of absorbing at least 163,350 lb-in at the 750 position.
T520B DATA INPUT I.
19.58 1.000 1.750 5.500 0
0 70 85 74 CYLINDER DIAMETER Cin)
CENTER OR TIE BAR DIAMETER Cin)
PISTON ROD DIAMETER Cun)
NUMBER OF PISTONS =
MOMENT ARM CIn)*
SPRING LOAD A Clbs)=
SPRING LOAD B (lbs)=
BREAK EFFICIENCY ()
RUNNING EFFICIENCY C%>
=
ENDING EFFICIENCY C1)
- PRESSURES (psi) 40 ACTUATOR TYPECB-1,HD=2,T,TR=3, =
YOKE ARM SPRING ANGLE TORQUE Cdegrees)
(in lb) 0 0
5 0
10 0
15 0
20 0
25 0
30 0
35 0
40 0
45 0
50 0
55 0
60 0
65 0
70 0
75 0
80 0
85 0
90 0
PRESSURE TORQUE C
40)psi 91515 81533 73965 68195 63811 60533 58170 56595 55727 55523 55975 57106 58975 61681 65379 70301 76785 85340 96745 PRESSURE PRESSURE PRESSURE TORQUE TORQUE TORQUE C
60)psi C
80)p5i C 90)p5i
£37273 183030 205909 122299 163066 183449 110947 147929 166420 102292 136389 153438 95716 127621 143574 90799 121065 136199 87255 116340 130883 84892 113190 127339 83590 111454 125385 83285 111047 124928 83963 111951 125945 85660 114213 128489 88462 117949 132693 92521 123361 138781 98069 130759 147103 105451 140602 158177 115177 153570 172766 128010 170680 192015 145117 193489 217675 EFFICIENCY SPR.
PRES.
74 70 77 73 79 76 81 78 82 80 83 82 84 83 as 84 85 85 85 85 85 85
'84 85 83 84 82 83 80 82 78 81 76 79 73 77
/0 74 60 80 90 3-
- 15208, page 2 I.................................
188~~
EFFICIENCY PLOT EFFIClENCY vs ANGLE fm
~~~...................................................
(0 t..D7 2ii0.......................
P...........
O n
21 0 0............
8.......I.
8
.8 1015
-6 L.......................
3.8..............
YOE A40PANGL
.1..
i...
L~C Lf~L C.......................
c.
ATTACHMENT 4
SUPPLEMENTAL TORQUE CALCULATIONS
ATTACHMENT 4 The following pages illustrate the combined effects of disc blockage and delay time on dynamic torque.
In each case, the delay time is fixed at that which produced the worst case torque for the full open, unblocked condition. The initial disc angle is reduced by blocking to illustrate the resultants of several different initial angles of opening.
or D-29254-1 JOB: FLOR. Pup; 'CRYST. RIv P2-VAPIABLE SIZE ADJUSTED :REYNLD: NO.FNCTN!)
SAT.STEAM/AIR MIXTURE ITH 1.4 LE:
STEAM PER 1-LES AIR SPEC.G.
.738255 MOL.WT.= 21.3872 KAPA:ISENT.EXP.
1.19775 GAS CON MM=.TANT-
- ALC.
sorne SPEED KNOVING NIXTR.)= 1316.65)
FEET-'SEC AT-225 DEG.
CRIT.CAS E INLET VELOCITY IS 1.46694 5 INCH MODEL R= 72.1972 TIMES HIGHER AS AIR CRIT.CASE INLET Vi-OF MAX.
TORQUE IS AT THE CRITICAL PRESS. RATIO(.585- (5 IN.MODEL OR APPX
.695051
( 47.375 IN:)WITH.TMIX.)FIRST soNI 7
2 PEG.'.A.)
ABSOL. MAX. TORUE* FIRST SONIC)AT 72-68 DG.VLV.ANG.=
171483 IN-LBS
- p 35 DEG.
MAX.TORUE INCLUDES SIZE EFFECT(REYNOLDS NO.ETC)APPX.
2 1.16482 FOR 47.375 INCH BASIC LINE I.
ALL PRESSURES USEr'STHTICCTAP)PRESHIBOLUTE;P2 INCL.RECOV'ERY PRESS.
(TORQUE) CALC'S VAL I DI TY: P1 P2> 1. 07; VALVE TYPE:
48"-R1A;16 CLASS 75 DISC SIZE:
46.718 INCHES OFFSET ASYMMETRIC DISC SHAFT DIA.:
4.75 IN' HE.
ERG.
COEF.
OF FRCTN.:
- 5. CC000E-03 SEATING FACTOR:
15 INLET PRESS.
.AR.
MA:.:
4 PSIA OUTLET PRESURE P6) 23.5 PSIA (72 DEG.
ACTUAL PRESS. ONLY 'AR.::
MAX. ANG. FLOW RATE:
98904.2 CFM; 121031.
665*;
- 65.
4:3 LFBM-IN CRIT.SONIC FLOW-90DG: 36162.3 LB. MIN AT 19.1166 INLET
.SIA LMIN VALVE INLET DENSITY:
6.72714E-02 LBxFT^3-MIN.
.104519 LE7FT~
MA FULL OPEN DELTA P:
- 5. 75262 PSI SYSTEM CONDITION:
PIPE IN-PIPE-OUT -AND-AIR/STEAM MIXTURE SERVICE :l 225 DEG.F MINIMUM 0.75 DIAM.
PIPE DO..INSTREAM FROM CENT.LINE SHAFT.
P1 ABS.
PRESSURE<AD.)FOLLOWS TIMEXPRESS. TRANS.IENT CURVE.
ABSOLUTE MAX. TORQUE IS DEPENDENT ON DELAY TIME AND 3.43 TO 2. 15-TH POWER OF (P
P:2) IN IJORST RANGE X LINEAR CONSTANT X. Dl.WNSTR.PRES:.
P6-ABS. (75-
.DEG.
IN SUBSONIC RANGE LIMITS-ONLY;SEE FORMULATION;.-PER TESTS H. PRATT THIS TO.
AT 72 DEG.:YMM.
DISC (68=OFF;ET SHAFT)CTT/D^3 P2(ABS)
-- 5 IN.MODEL E'PUIV.VALUES------ACTUAL SIZE VALUE:;
ANGLE P1 P2 DELP PRESS.
FLOW FLO" TD TE+TH TINE APPRN.PSIA PSIA PSI RAT
- .:CFM)
(LBMIN j NCHLES----
TP-TE-TH 35 23.70 15.:4 7.86
.669 121031 6653 26296 115 26110 30 26.92 14.30 12.12
.550 106855 574 22622 17 22434 25 29.02
- 14. 76 14.26
.509
- 6530 4756 13 39
- 3 1:3 073, 20 30.12 14.73 15.39
.49 2561 2889 14270 3
13997 15 30.46 14.71 15.76
.483 2632 1574 10 31.98 14.70 17.28
.40 14:6:
317 73 384 471:
5 34.4S 14.70 19.78
.426 4620 24 356 445 3410 0 36.32 14.70 22.12
.3.9 0
0 34116 40 33665 SEATING
+ BEARING +
HUB SEAL TORQUE
'M N' -
34116 IN-LI*
- D C PEG.
MA.
PiDN.
=-
26296 IN-LB:
'i 5 PEG.
.550.106855 587 (LO CA::
SEC.
1.00
- 1. 42 1.76 1.95
- 2.
14 A
SUMMARY
TORQUE TABLE-VALVE BLOCKED TO: 40 DEG.
r MAX.ANG.FLOW RATE:
133998.
CFM; 163977.
SCFM; 9014.24 LBxMIN SEATING
+ BEARING
+ HUB SEAL TORQUE CMt
- 44PI-Bi 0 D EG.
MAX. IH.
BEARING
-HUB EAL TORQ1UE 1M-M) 42734 IN-LBS "
40 DEG.
AT 1
SEC.DELAY TIME TO 3.22222 CLOSED VLV.
TIME( 23.?
TO 38. 57 SIA UPSTR.PRESS.)3.
REYNLDC NO.FACTOR 'PMULTIPL.)=
1.31498 TOTAL TO.IICREASE-FACTOR:TO MODEL BASIS)-F-(RE) +P6-P2>)J9=
1.44557
SUMMARY
TORQUE TABLE-VALVE BLOCKED TO:
45 DEG.
MAX.ANG.FLOW RATE:
166950.
CFM; 204300.
SCFM; 11231.
LBZMIN SEATING + BEARING
+ HUB..SEAL TORQULE (M-Jt 3 4172 IN-LBS.;"l 0 BEG.
MAX.DYN.
BEARING
';x)=
68292 IN-LBS
'P 40 DEG.
TR1P SEC.DELAY TIME TO 3.5 CLOSED VLV. (LOCA) TIME(
23.7 TO 39.6 PSIA UP STR. PRE:-3S REYNLDS NO. FACTOR (MULTIPL.::*=
1.34852 TOTAL TORO. INCREASE-FACTOR (TO MODEL BASIS) -F (RE) *'P6/P2) *J9=
- 1. 48244
SUMMARY
TORQUE TAELE-VALVE BLDCKED TO: 50 DEG.
MAX.ANG.FLOW RATE:
205708.
3 LE-tIN SEATING. + BEAI"IG + HB SEAL T ORQE M'M)
=
4201 Ir-LB:'
0 BEG.
MAX.DI-N.
BEARING HUB P-EAL TORQUE c'M-M J 89725 IN-B
- 45 BEG.
A IA SEC.ELAy TIME TO 3.77778 CLOSED VLV. (LOCA)TIME*:
23.7 TO 41.0175 PSIA UPS T.PRES'S.)
PEYNLDS2 NO. FACTOR (MIULTIPL.)= 1.31623 TOTAL TORQ.INCREASE-FACTOR(TO MODEL BASIS-FIRE)*(P6.P2)+J9-1.44695
SUMMARY
TORQUE TABLE-VALVE BLOCKED TO: 55 DEG.
MAX. ANG. FLOW RATE:
253658.
CFM; 310407.
- SCFMI 17063.
LB-MIN
.:EAT IN'G
+ BEARINHG
+ HUB
- EL TRU M')-
329I-E ABG MAX.D rN.
-BEARING HUB PEAL TORQUE it~
N)=1392I-B.:49BG AT 1
CEC.DELAY TIME TO 4.0555 CLOED L
.LDCA TIME 2
TO 42.4069 PSIA UPSTP.PPE.
REYNLDSp NO.FACTOPR(MULTIPL.:=
1.0717 TOTAL TORQ. INCT REASE-FAC TOR TO MODEL BASIS:'-F RE.:*+P6/P2)+J-=
1.43698
b
SUMMARY
TORQUE TABLE-VALVE BLOCKED TO: 60 DEG.
MAX.ANG.FLOI RATE:
303125.
CFM; 370942.
SCFM; 20391.7 LB/MIN SEATING
+ BEARING + HUB SEAL TORQUE (M-M)=
34257 IN-LBS -P 0 DEG.
MA:X.DYN.
BEARING HUB SEAL TORQUE (MAM) 150084 IN-LB; i 55 DEG.
AT 1 SEC.DELAY TIME TO 4.33333 CLOSED VLV.(LOCA)TIME(
23.7 TO 43.7648 PSIA UPSTR.PRES.)
.REYNLDS NO.FACTOR(MULTIPL.)=
1.29943 TOTAL TORC.INCREASE-FACTOR(TO MODEL BASIS)-F(RE)*(P6zP2)+J9=
1.42848
SUMMARY
TORQUE TABLE-VALVE BLOCKED TO: 65 DEG.
K MAX.ANG.FLOU' RATE:
362164.
CFM; 443138.
)L SEATING + BEARING
+ HUB SEAL TORQUE (MM)=
34284 IN-LS 9 0 DEG.
MAX.DYN.
BEARING HUB SEAL TORQUE (MM)
=
1:388248 IN-L-BS ;; 55 DE'.
AT 1 SEC.DELAY TIME TO 4.61111 CLOSED VLV.(LOCA:TIMEC 23.7 TO 45.0363 PSIA UPSTR.PRESS.)
REYNLDS NO.FRC TOR(MULTIPL.)=
1.28947 TOTAL TORO.INCREASE-FACTOR(TO MODEL BASIS)-F(RE)+(P6AP2).J9=
1.4175:3
SUMMARY
TORQUE TABLE-VALVE BLOCKED TO:
70 DEG.
MAX.ANG.FLOLJ RATE:
405528.
CFM 496253.
SCFM; 27280.4 LB/MIN SEATING
+ BEARING + HUB SEAL TORQUE (M'M:=
- 34310 IN-LES @
0 DEG.
MA:-:.DYN.
BEARING HUB SEAL TORQUE (M4M:)
=
264620 IN-LBC:
- i' 65 DEG.
AT 1
SEC.DELAY TIME TO 4.88889 CLOSED VLV.(LOCA)TIME(
23.7 TO 46.367 P
SIR UPSTR.PRE:;.)
REYNLDS NO.FACTOR 'MULTIPL.)=
1.26626 TOTAL TOROi:.INCREASE-FACTOR(TO MODEL BASIS)-F(RE)*(P6-P2)*J9=
1.39201
b
SUMMARY
TORQUE TABLE-VALVE BLOCKED TO:
75 DEG.
MAX.ANG.FLOW RATE:
476489.
CFM; 5S3090.
+
BEARING +
HUB SEAL TORQUE J:M-M:) =
- 34335 IN-L.:
0 DEG.
MAX.Di'N.
FEARING HUB SEAL TORQUE (M.M)
=
- 331 197 IN-LB:S -@ 65 DEG.
AT 1 SEC.DELAY TIME TO 5.16667 CLOS'ED VLY.:.LOCA) TIME(
23.7 TO 47.594 PSIA UPSTR.PRESS.)
REYNLDS NO.FACTOR*'MULTIPL.)=
1.2569.
TOTAL TORO. INCREASE-FAC::TOR (TO MODEL BASIS) -F*:RE.**(P6P2:>+J9=
1.38181
SUMMARY
TORQUE TABLE-VALVE BLOCKED TO: 80 DEG.
MAX.AING.FLO.I RATE:
496742.
CFMS 607875.
S&CFM 33416.5 LB/MIN SEATING + BEARING + HUB :EAL TOR17UE
-:.MM)=
3439 CPU STEP LIMIT OF 20 EXCEEDED IN.STEP VARTOBL1 ENTER NEW LIMIT -- 35 IN-LSB
-it 0
DEG.
MAX.DYN.
BEARING -
- M')r
=
337114 IN-L@S 65 DEG.
AT 1 SEC.DELAY TIME TO 5.44444 CLOSED VLY. (LOCA::'TIME(* 23.7 TO 43. 76019 PSIA UPSTR.PRESS.)
REYNLDS. NO.FACTOR(riULTIPL.:*=
1.25024 TOTAL TORIO'.I NCREAS.E-FACTOR (TO MODEL BASIS)-F(RE)**:P6zP2: +JS= 1.3744
SUMMARY
TORQUE TAEBLE-VALV..E BLOCKED TO: 35 DEG.
MAX.ANG.FLOWI RATE:
526939.
CFM; 644 28.
SCFM; 35447.9 LE-MIN SEAT I NG + BEARING
+ HUE SEAL TORQUE 8M 4381 IN-LES @9 0 DEG.
MAX.DYN.
EEARING' -
- MzM)
=
416576 Ir-LB
- 65 DEG.
AT 1
CEC. DELAY TIME TO 5.72222 CLOSED VLV.:. LOCA) TIME: : 23.7 TO 49. 3322 PSIA U1PSTR.PRE:SS.)
REYNLDS NO.FACTORPMUILTIPL.:)=
1.24543 TOTAL TORO..INCREASE-FACTOR*:TD MODEL BA:IS)-F(RE:)+*:P6/P2J9=
1.36912
ATTACHMENT 5 GENERAL ARRANGEMENT ANP CROSS SECTION DRAWINGS