ML18031A360
| ML18031A360 | |
| Person / Time | |
|---|---|
| Site: | Susquehanna  |
| Issue date: | 03/09/1982 |
| From: | Ballun J, Kaza R, Wrona T BECHTEL GROUP, INC. |
| To: | |
| Shared Package | |
| ML17139A731 | List: |
| References | |
| RTR-NUREG-0737, RTR-NUREG-737, TASK-2.E.4.2, TASK-TM D-0026-1, D-26-1, NUDOCS 8206160257 | |
| Download: ML18031A360 (121) | |
Text
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SOLATION/PURGE VALVE ANALYSIS FOR 24"-1200 BUTTERFLY VALVE Project Site Sus uehanna Steam Electric Station Berwick Penns lvania Customer Penns lvania Power & Li ht Engineer Bechtel Power Cor oration Specification No. 8856 Original Purchase Order 8856-P-31-AC Original Pratt Job No. D-0026-1 Valve Tag Nos. HBB-BF-AO-5713 i HBB-BF-AO-5714 HBB BF AO 5722 g HBB BF AO 5723 General Arrangement Draw'ings C-2598 Rev. 5 Cross Section Drawing C-2987 Rev. 2
'repared by: . Oltllliililtllll Date:
Reviewed by: REGISTERED PROFESSIONAI.
Date: ENGINES
~ oa Certified by: ~
'<,'<LiXO~ "
Date: ""'llllltlllllilOO PDR ADOCK 05000 E
CONTENTS Pacae I. Introduction II. Considerations III. Method of Analysis A. Torque Calculation B. Valve Stress Analysis C. Operator Evaluation 9 IV. Conclusion 10 V. Attachments (1) Input Documents (A) Pressure vs. Time Graph (B) Customer/Engineer Response to Request for Information (2) Valve Assembly Stress Report (3) General Arrangement and Cross-Section Drawings
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 I'he absence of definitive input.
"ZX. 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.l. 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 customer/engineer is utilized in calculations.
Downstream pressure vs. LOCA time is assumed to be worst case.
- 3. Worst cas'e 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 present 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 which were not furnished with .purge valves evaluated in this report.
768. 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 this report, worst case conditions have been applied to the analysis; namely, 90 elbow (ups tream) oriented 90 out-o f-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 analysi's consists of a'static analysis'f 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 readiation resistance of 1 x 10 rads at a maximum incidence temperature of 350 F. It is recommended that seats be visually inspected every 18 months and be replaced periodically as required.
Valves at outside ambient temperatures below 0 F, if not properly 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.
l 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 II, angle.
Bearing friction s
torque is calculated from the following equation:
TB=P xAxUxd where P =pressure differential, psi 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 i RCR > 1 >
P2
- l. 07 (approx. )
T = D3 x CTl x P2 x K x F D
For sonic flow l CR P2 T =D 3 xCT2xP2x K xF~
l.4 RE Where T
D
= fluid dynamic torque, in-lbs.
F~ = Reynold number factor RCR
= critical pressure ratio, (f (~) )
Pl upstream static pressure at flow condition, psia P2. downstream static pressure at flow condition, psia D = disc, diameter, in.
C Tl1 = subsonic torque coefficient CT2 = sonic torque coefficient K = isentropic gas exponent ( 1. 2 for air/steam mix) 0 = 0 = fully
= disc angle, such that 90 fully open; 0 closed Note that C Tl1 and CT2 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 Pl 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 0
coincident with a disc angle of 72 0 (symmetric) or 68 (asymmetric) from the fully closed position.
The following computer output summarizes calculation data and torque results for valve opening angles of 90 0 to 0 0
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' 'I J / Oc JOB:SUSQUEMAHA/BECHTEL SAT.STEAM/AIR MIXTURE WITH 1.4 LBS STEAN PER 1 "LBS AIR SPEC.GR.= .738255 NOL.ffT.= 21.3872 NAPA(ISEHT.EXP.)= 1.19775 R= 72.$ 972 GAS COHSTAHT-CALC; SOHIC SPEED(NOVIHG MIXTR.)= 1354.57 FEET/SEC AT 265 BEGS ABSOL.MAX.TORQUE(FIRST SOHIC)AT 72-68 DG.VLV.AHG.= 64426 IH-LBS e 68 DEG.
MAX~ TORQUE IHCLUDES SIZE EFFECT(PEYHOLDS HO.ETC)APPX. X 1.31542 FOR 24 IH CH BASIC LIHE I.D.
ALL PRESSURES USED:STATIC(TAP)PRESS.-ABSOLUTE;P2 ItiCL.RECOVERY PRESS.
(TORQUE) CALC'S VALIDITY:P 1/P2) $
07'ALVE TYPE: 24"-1200 CLASS 150 DISC SIZE:,
SHAFT DIA.:
. 2$ .7 3
INCHES IHCHES OFFSET ASYMMETRIC DISC BEARIHG TYPE: BROHZE SEATIHG FACTOR: .
'1 5
IHLET PRESS.VAR.)lAX.: 48.2 PSIA OUTLET PRESSURE(P6): 28 PSIA (72 DEG. ACTUAL PRESS.OHLY(VAR.))
MAX.AHG.FLOff RATE: $ 24950. CFN; 304169. SCFM; 16721. LB/NIH .
CRIT.SOHIC FLOU-90DG: 14217.9 LB/NIH AT 3$ .2534 IHLET PSIA VALVE IHLET DEHSITY: . $ 338~$ 'B/FT" 3-MIH..12'9262 LB/FT "3-NAX.
FULL OPEH DELTA P: 20.8378 PSI SYSTEM COHDITIOHS:
PIPE IH-PIPE-OUT -AHD- AIR/STEAN MIXTURE SERVICE 8 265 DEG.F NIHINUN 0.75 DIAN. PIPE DOMHSTREAN FROM CEHT.LIHE SHAFT.
Pl ABS. PRESSURE(ADJ.)FOLL0$ 8 TIME/PRESS.TRANSIENT CURVE.
--5 IH.NODEL EOUIV.VALUES "-ACTUAL SIZE 'VALUES" AHGLE Pl P2 DELP PRESS. FLOW FLOM TD TB+TH TINE (LOCA)
APPRX.PSIA PSIA PSI RATIO (SCFN) (LB/MIH) -"IHCHLBS- - TD- TB-TH SEC.
90 48.0$ 24.66 23.35 .514 CR 304169 16721 27057 1700 25357 5.00 85 48.02 24.7f 23.31 .515 CR 331571 18227 35348 2221 33126 7.60 80 48.03 24.30 23.73 .506 321895 17695 30397 1'910 28487 $ 0.13 75 48.04 23.33 24.71 .486 CR 305389 16788 49244 3094 46150 12.50 72 5$ .68 22.06 29.62 .427. CR 278174 15292 64229 4036 60193 13.82 70 48.05 21;57 26.48 .449 CR 268299 14749 57808 3632 54175 14.64 65 48.06 $ 9.87 28.19 .414 CR 229424 12612 53183 3342 49841 16 ~ 49 60 48.07 18.45 29.62 .384 CR 196702 10813 42987 2701 40286 17.99 55 48.08 17.$ 9 30.89 .358 CR $ 63229 8973 38264 2404 35859 $ 9el0 50 48.09 16.41 31.68 .341 CR $ 32168, 7265 30733 2602 2813 I 19.77 45 48.10 15.87 32.23 .330 128773 7079 26623 2862 23760 20.00 40 48.$ 'I $ 5.51 32.60 .322 89185 4902 19274 3139 16134 20.23 35 48.12 15.14 32.98 .315 67630 37f7 12434 3292 9141 20.90 30 48.13 14.93 33.20 .3$ 0 49527 2722 7039 3485 3553 22.01 25 48.14 14.81 33.33 .308 33942 1865 4458 3730 727 23.5$
20 48.15 $ 4.75 33.40 .306 20783 $ 142 2950 4174 "1223 25.36 15 48.16 14.71 33.45 .305 12040 6&1 1026 4703 -367? 27 '0 10 48.17 12.99 35. 18 .270 5634 309 546 5317 -4770 29.87 5 48.18 11.32 36.86 .235 1847 101 360 5646 -5286 32.40 0 48.20 14.70 33.50 .305 0 0 13286 4646 8640 35 00F SEATIHG + BEARIHG 4 HUB SEAL TORQUE (M/M)= ~
13286 IH-LBS e 0 DEG.
MAX.DYH. - BEARING - HUB SEAL TORQUE (M/M) = 64229 IH-LBS 8 70 DEG.
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') 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 I
formula:
Smax = 3; (Tl+T2) + 1 (Tl+T2) + 4 (Sl+S2) 2 2 where Smax = maximum combined stress, psi Tl = direct tensile stress, psi I
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 52, 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.
C. Operator Evaluation Model: Bettis . T416-SR3 Rating: 107,700 in-lbs at full 'open and closed positions only.
71, 100 in-lbs at 6 8 59,800 in-lbs at 45 (minimum rating).
Maximum Valve Torque: 64,426 in-lbs at 68 0 The maximum torque generated during a LOCA induces reactive forces in the load carrying components of the actuator.
Since the LOCA induced torque derived in this analysis is less than the maximum absorption rating of the operator, it is concluded that the Bettis models furnished are structurally suitable to withstand combined LOCA and seismic loads.
10 IV. Conclusion It is concluded that the valve structure and the valve actuator are both capable of withstanding'ombined seismic and LOCA-induced loads based on the calculated torques developed in this analysis.
ATTACHMENT 1A PRATT PROPOSAL LETTER
HK&HY PHATT COhlPANY
('t(.,"ttii'( ( t., ~it)( ( t it) ~ l()t I ltti(l <<x<<t(.rtl>>
401 SOUTH HIGliLANDA~US AURORA+ tLLIa IOIS 8OGO7 April 16, 1981 Bechtel Power Corporation P.O. Box 3965 San Francisco, CA 94119 Attention: Mr. E.B. Poser
.. Project Engineer
SUBJECT:
Susquehanna Stean Electric Station Containment Isolation/Purge Valve Analysis Gentlemen:
'ith reference the valves and to your recent inquiry regarding suitability of actuators to withstand aerodynamic LOCA conditions, please note the following:
Torque calculations will be performed for aerodynamic torque generated as a result of LOCA. These calcula-tions will be performed using the following data to be furnished by you.
A. Containment Pressure Time Curves B. Containment Temperature - Time Curves C. The combined resistance coefficient for all '-
ventilation system components downstream of the valve (one for'ach valve size) or A graph of back pressure vs. LOCA time at a distance 10-12 diameters downstream of the valve. Consider also the capacity of the piping, filter and duct work to resist increases in back pressure.
D. Maximum and minimum delay times from LOCA to initiation of valve rotation.
E.. Drawings or written description of valve
~ 'rientation with respect to elbow immediately upstream of valve (within 6 d'ameters), as well as direction of valve closure (clock-wise or counterclockwise) as viewed. from operator end.
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Bechtel Power Cc,. adoration Page 2 April 16, 1981 THATTt Iv Xn the absence of the above information, the following assump-tions will apply to the purge valve analysis.
- l. 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 condi-tion and critical valve disc angle to coincide, resulting in maximum possible dynamic torque.
- 3. 90 elbow immediately upstream, oriented 90 qf-plane with respect to valve shaft, with leading edge of disc closing away from'outside radius of elbow. Such orientation and closure will increase torque values by 20% or more.
- 2. Based on the above results, a static load stress analysis will be provided for valve components affected by the dynamic torque loadings in combination with'pressure and seismic loads.
The actuator supplier will be asked to verify the suitability of the actuator or the reaction ox'ack drive fo ce resulting I /
from aerodynamic torque conditions.
The cost of performing the 'evaluation will be $ 12,800 each size or 6", 18" of the valve components 3~
and 24" valves.
4~ The completion of this analysis is projected'to be twenty-six (26) weeks after receipt of p'urchase order 'and data requested above based on availability of engineering schedule.
5, Our response to NRC's criteria for operability
'of purge valves is included in the demonstrating analysis.
This proposal is for investigative analysis only and is not intended 6o guarantee the adequancy of the equipment as fur-nished when subjected to LOCA loads currently being defined.
will be Net 30 Days.thirty (30) days.
The proposal <<s valid for The terms of payment He hope you will find the proposal responsive to your needs. Ef we can be of any additional assistance in this matter, please advise.
Very truly yours, HENRY PRATT COMPANY
//kL~
L. Beane 'lenn GLB/tl Hanager-Application Engineering
ATTACHMENT 1B CUSTOMER/ENGINEER RESPONSE TO REQUEST FOR INFORMATION
happ) F "vfff ) Ft'-"'~-'echtel Power Corporation Engineers-Constructors Henry Pratt Company Fifty Scale Street 401 South Highland Avenue San Francisco. California Aurora, Illinois 60507- MdaAddreddr p.o. Box 3965. san Francisco. GA 94119 Attention: Mr. G. L. Beane
'( 1" ' 4ggp ~<
Subject:
Susquehanna Steam Electric Station Units 1 and 2 Job 8856 Gentlemen.
P.O. 8856-P-31-AC, Containment Isolation/Pu e Valve Anal sis gQ 5'e In order to perform the analysis Henry Pratt requested certain information.
The following is our reply:
A. Containment pressure time curve is attached.
B. Containment terrperature time curve is attached.
C. A back pressure of 19.7 psia should be used in this analysis. %is back pressure is per the assumptions in your letter 'of April 16, 1981.
D. Minimum delay time is 0.1 seconds. Maximum delay time is 5 seconds.
E. Isometric drawings for both units are attached. We believe that Henry Pratt is in a better position to determine the direction of valve closure as viewed from the operator end. This information is not apparent on the drawings you submitted to Bechtel.
In addition, if Henry Pratt's 16 week analysis report shows the valves to be unctualified, Henry Pratt will state at what angle the valves must be blocked open in order to meet the NRC's interim position. Henry Pratt will also make recommendations on how to block the valves and to provide a detailed drawing of the stop.
We trust that the foregoing information is satisfactory and will enable you to complete the qualification of the subject valves. If you have any questions, please contact Al Daily at (415) 768-9235 or A. Tiongson at (415) 768-7770.
Very truly yours, E. B. Poser Project Engineer Written Response Req'd: No Design Document Changes: No CHN/APT/cgs WP30/3-1 cc: Mr. T. M. Crimmins, Jr. (PL) w/a 502 d
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ATTACHMENT 2 Hu~ffm~v KC fPMMM
. Rn~II@aia l
SEISMIC ANALYSIS FOR 24 INCH NUCLEAR PURGE VALVE
j ~ ~
TABLE OF CONTENTS
~Pa e List of Fi ure's Nomenclature Srrmm .b 18 Stress Level Summary 20 Frequency Analysis Summary 24 Valve Dimensional Data 25 Stress Anal sis 28 27'ntroduction End Connection Analysis 32 Body Analysis 33 Disc Analvsis 39 Shaft Analysis 42 Disc Pin Analysis 44 Sh:rft Bearing Analysis 45 Cover Cap Analysis 46 Thrust Bearing Analysis Operator hlounting Analysis 50 I:r'e uencv Anal ~is (Valve Component~) 58
30
~
. LIST OF FIGURES
~Fi .No'. Title ~pa e Valve Body Spatial Orientation 29 Va3.ve C ros s - Se ct i on 31 Pressure Area Analysis Cross- 34 Section in Crotch Region 4 Pressure Area Analysis Cross-. 37 Section'n Body'isc 40 Bottom Trunnion Assembly 47 Top Trunnion i~lounting .51 Trunni'on Bolt Pattern 53
~
Operator Holt Pattern 54
30 VOhfENCLATURE The nomenclature for this analysis is based upo n the nomenclature established in Paragraph NB-3534 of Section III of the ASi~lE Boiler and.Pressure Vessel Code. Yfhere the nomenclature comes directly from
. the 'code, the reference paragraph or figure. for that symbol .is given with the definition. .For symbols not defined in the code, the definition is that assigned by Henry Pratt Compa'ny for use in this analysis.
1
30
.ANALYSIS NOl IENCLATURE Af Effective fluid pressure area based on fully corroded
- interior contour for calculating crotch primary membrane stress (NB-3545. 1(a)), in2
<m Metal'area based on fully corroded interior contour effective in resisting fluid force on Af (NB-3545.1 (a)), in-A3 Tensile area of cover cap bolt, in.
A4 ~
Shear area of 'cover cap bolt, in A5 Tensile'rea of trunnion bolt., in A6 Shear area of trunnion bolt, in A7 Tensile area of operator bolt, in 1
A8 Shear area of operator'bolt, in2 Bl Unsupported shaft length, in.
B2 Bearing bore diameter, in.
B'3 Bonnet bolt tensile area, in2 B4'5
~ Bonnet bolt shear area, in'2 Bonnet bodv cross-sec'tional 'area,. in2
'6 Top bonnet weld size,,in.
B7 Bottom bonnet weld si e, in.
Distance to outer. fiber of bonnet from shaft on
~
y axis, in.
B9 Distance to outer fiber of bonnet from shaft on x axis, in.
A factor depending upon, the method of att'achment
~
of hoad, shell dimensions, and other items as listed in NC-3225.2, dimensionless (Fig. NC-3225.1 thru Fig. NC-3225.3)
ANALYSI S NOMENCLA'7URE Stress index for body. bending secondary stress re-sulting from moment in connected.'pipe (NH-3545.2(b))
'C Stress index for body primary plus secondary stress, inside surface, resulting from internal pressure (NB-3545.2(a))
Stress index for thermal secondary membrane stress resulting fr'om structural discontinuity C3 Stress index for maximum secondary membrane plus bending stress resulting'rom structural discontinuity C6 . Product of Young's modulus an/ coefficient of linear thermal expansion, at 500oF, psi/ F (NB-3550)
C7 Distance to outer fiber of disc 'for bending along the shaft, in.
C8 Distance to outer fiber of disc for bending about the shaft, in.
'Cg Distance to outer fiber of flat plate of disc for.
bending of unsupported flat plate, in.
Inside diameter of body neck at crotch region (NB-3545.1(a)), in.
dm .Inside'iameter used as basis for determining body
~
minimum wall thickness, (NB-3541) in, Valve nominal diameter, in.
D2 Shaft diameter, in.
D3 Disc pin diameter,'n.
'4 Thrust collar outside diameter, in.
Ds Spring pin diameter, in.
D6 Cover cap bqlt diameter, in; .
D7 Trunnion .bolt diameter, in.
30 ANALYSIS NOMENCLATURE Ds Operator bolt diameter, in..
Dg Bonnet. bolt. diameter, in.
Modulus of .elasticity, psi Fb. . Bending modulus of standard connected pip~, as given by Figs. NB-3545. 2-4 and NB-3545. 2-5, in.
Fd ~
1/2 x cross-sectional area of standard connected pjpe, as given by Figs. NB-3545.2-2 and NB-3545.2-3, in.
Natural frequency of respective assembly, hertz Fx N3gx- -Seismi'c force along x axis due to seismic accelerat'ion acting on .operator extended mass, pounds Fy N3gy-'-Seismic force ,along y axis due to seismic acceleration acting on operator extended mass, pounds F- N3gz-'- Seismic force along z axis due to seismic acceleration acting on operator, extended mass, pounds Gravitational acceleration constant, inch-per-second2 Gb Valve body section bending modulus at crotch region (NB-3545. 2 (b) ), in3 Gd Valve body section area at crotch pegion '(NB-3545.2 (b) ), in Gt Valve body section torsional modulus at'rotch region
.'NB-3545.2(b)), in3 gx Seismic. acceleration constant along. x axis gy ,Seismic acceleration constant along y axis gz Seismic acceleration constant along z axis hg Gasket moment arm, equal to the radial distance from the .center line of the bolts.to the line. of the g'asket reaction (NC-3225), in.
H2 Top trunnion built square, in.
.. H3 'Bottom trunnion bolt square, in.
ANALYSIS NOMENCLATURE H4 ,Bonnet bolt s'quare, in.
Hs Operator bolt square, in.
Bonnet bol't circle, in.
Operator bol't circle, in.
Hs Bonnet height, in.
Hg Actual body wall thickness, in.
Bonnet body moment of inertia .about x axis, in4 I2 Bonnet body moment of inertia about y axis, in4 I~ Disc area moment -of inertia for bending about the shaft, in4 I
I4 Disc .area4moment of inertia for bending along the shaft, in Momen't of inertia of valve body, in4 Nomen't o f inertia o f sh a ft , in 4
. Dz. s c area momen't f in e rg4 ia for bending of un-supported fla t plate , in Distance t o neutral bending axis for t op trunnion bolt pat t ern along x axis , in .
Distance to neutral bending axis for top trunnion bolt pattern along y axis, in.
Distance. to neutral bending axis for bonnet bolt pattern along x axis, in.
Distance to neutral bending axis for bonnet bolt pattern along y axis, in.
Distance to neutral bending axis for operator
'bolt pattern along x axis, in.
Distance to neutral bending axis for operator bolt pattern along y axis, in.
Spring constant ANALYSIS NOMENCLATURE Kl D1.stance of bonnet leg from shaft centerline, in.
Thickness of disc above shaft, in.
Kp Length along z axis to c.g. of bonnet plus adapter plate assembly, in.
Top trunnion width,,in.
Kg Top trunnion depth, in.
K6 Height of top trunnion, in.
Ll -.Valve body face-to-face dimension, in.
L2 Thicknes's of operator housing under, trunnion bolt, in.
. Length. of engagement of cover cap bolts in bottom trunnion, in. E Length of engagement of trunnion bolts in top
. trunnion,'n.
Lg Bearing length, in, Lr. Length of structural disc hub welds, 'in. N
'L7 Length of engagement of bonnet bolts in adapter plate, in.
Lg of engagement of bonnet bolts in bonnet,
'ength in ~
Lg Length of engag'ement of stub shaft in disc, in.
Reciprocal of Poisson's ratio
~ iilass o'f component hfx tit3 (gvZo+gzYo), operator extended mass seismic bendi.ng moment about the x axis, acting at the base oP tl>e operator, in-lbs.
My N3 (gxZo+gzXo) operator extended mass seismic bending inomont about the y axi s, acting at the base of the operator, in-lbs.
ANALYSIS NOh)ENCLATURE hlz .ltd (gx Yo+gy Yo}, operator extended mass seismic bending,moment about the z axis, in-lbs.
hlx Mx+FyT5, operator extended mass seismic bending moment about the x axis, acting at the bottom of the adapter plate, in-lbs.
ihfy
=-
My+FxT5, operator extended mass seismic bending moment about the y axis, acting at the bottom of
'the adapter plate, in-lbs.
hlx
'f Mx+Fx(T5+H8)+gxN41'3,'perator extended mass seismic bending moment about the x axis, acting at the base the bonnet',
'ly in-lbs.'y+Fx(T5+Ha}+gxlIt4K3, oPerator extended mass seismic bending moment'bou't the y. axis, acting at the base of the bonnet,. in-lbs.
Bending moment at joint of flat plate to disc hub, in-lbs. P
'ermissible number of complete start-up/s'hut-down
'ycles 'at hr/100oF/hr/hr fluid'emperature change rate (NB-3545 ')
Not app'licable to ..t'e analysis of the system Number of top disc pins
,N2 Number of operator bolts iV3 Number of trunnion bolts Pd Design pressure, psi Primar> pressure rating,-pound Standard calculation pressure from Fig. NB-3545.1-1, psi Pe Largest value among Peb, Ped, Pet, psi Secondary stre'ss in crotch region of valve body caused by bending of connected standard pipe, cal-culated according to NB-3545.2(b), psi
ANALYSTS NOMENCLATURE P.ed 'econdary stress ih crotch region of valve body caused by direct or axial'oad imposed'y connected standard piping, calculated. according to NB-3545.2 (b), ps i Pet Secondary stress in crotch region of valve body caused by twisting of connected standard pipe, cal-culated according to NB-3545.2(b), psi Pm General primary membrane stress intensity at crotch region, calculated according .to NB-3545.1(a), psi Pm'p Primary membrane stress intensity in body wall, psi Sum of primary plus secondary stresses at crotch resulting from internal pressure, (NB-3545.2(a)),
P psi 4
QT Thermal stress in crotch region resulting from 100oF/hr fluid temperature change rate, psi Maximum thermal* stress component caused by through wall temperature gradient associated with 100oF/hr fluid temperature change rate (NB-3545.2(c)), psi Q72 Maximum thermal secondary membrane stress resulting from 100oF/hr fluid temperature change rate, psi QT3 'aximum. thermal secondary membrane plus bending stress resulting from structural discontinuity and'00 F/hr fluid temperature change rate, psi Mean radius of body wall at crotch region (Fig.
NB=3545.2(e)-1), in.
Inside radius of body at crotch region for cal-culating Qp (NB-'3545.2(a) ), in.
Fillet radius of external surface at crotch (NB-3545.2(a)), in. P R4 Disc radius, in.
Shaft radius, in.
Mean radius of body wall, R6 :Radius to 0-ring'n cover cap, in.
~'
30 ANALYSIS NOMENCLATURE Assumed maximum stress'n connected, pipe for calculating Pe (NB-3545.2(b)), 30,000 psi=
Design stress intensity, (NB-3533), psi Sum of primary plus secondary stress intensities at crotch region resulting from 100 F/hr temperature change rate (NB-3545.2), psi Spl Fatigue stress intensity at inside s'urface in crotch region resulting from 100oF/hr ft.uid temperature change rate (NB-3543.3), psi Sp2 Fatigue stress 'intensity at outside surface in crotch region resulting from 100 F/hr fluid temp-erature change rate (NB-3545.3), psi 7
S(l) through S(74) are listed after the alphabetical section.
te Minimum body wall thickness adjacent to crotch for calculating thermal stresses (Fig; NB-3545.2(c)-1),
in.
I tm . Minimum body wall thickness as determined by NB-3541, in..
Te. Maximum effective metal, thickness in crotch region for calculating thermal stresses, (Fig. NB-3545.2 (c)-l), in.
i BT2 Maximum .magnitude of the difference in average' wall temperatures for walls of thicknesses te, Te,
'resulting from 100oF/hr fluid temperature change rate, oF Thickness of cover cap behind bolt head, in.-
T2 ~
Thickness of shaft behin'd spring pin, .in.
T3 'Thrust collar thickness, in.
T4 Cover; cap thickness, in.
I5 Adapter plate .thickness, in.
ANAf.YSTS NA~ff!N('.I.ATUf<T!
T6 Tl)icl;ness oC bottom hon>>ct plate',
of t:op bonnet plate, in.
i'.'1)ick>>css T7
'I 78 h1axi)))u))) >'(;(fuirc(l operating torque for v:) lve, i.n-3 bs.
~ ~
of botto)i) bon>>vt weld, i>> 2 '
~
, Ul Area ~ I
( ~
U2 Area rof top bo>>nct weld., in
. Ug Sl)aft bearing coef'ficient of: friction U4 Bearing fr'icti.on torque due to prcssure loading (shaft journal hearings) I Ug Bearing'.fr1ct'Ron. torque due to pres'sure loading plus C'.
seismic loa(ling (shaft journal bearings) J'I I
U6 7hrust be" ring iri ction torque ~
I Distances to bolts i.n bolt pattern'on adapter. plate, in. 'Vl
'2 Dista>>ccs to bolt.". in bolrt pattern on adapter p3ate, in. Ii Vg Dist:anccs to bolt:s .in bolt pattern on adapter plat'e, 1>>, ( l
~
I V4 Dista>>ccs to bolts in bolt pattern on adapter plate, 1n ~
Dista>>ec to bolts in l)ol t pat:tern on bonnet, in, V6 Distanc'c to bolts in holt pattern on bonnet, in.
\
V7 Dist)>>c:c to bolts in b'ol t patter>> on bonnet, in..
L I VS Dist))>>cc to bol ts i>> bolt Lpattcrn on bonnet, in. rr
'f'ota1 l)ol.t, load, pounds Vn1vc woi t!1) ty po))>>(l::
I N2 lf))>> j v ) ('.i f!1)t,l)o))>>(l>>
OpcrLI t'()r bc.i gl)t, l)oun(ls llo))>>(Lt <<Il(l, (ldlll)t l f)ll)tc a)sso)))hly w(:zgl)t, pou>>ds C.
1<6 b'c'l (1 .':-:( o'f d i >>c>>t ructu):l l weld>>, i )) ~
I~
rr ~
I
~ ~
AMAI,YS15 NA"I'.."(: I,ATIIIll'.
I<'7 I"cij I'>t of di sc, pounds I:cngth of wc3d around perimeter of bonnet, in.
Xo I!cc'intrici t,: of center oE gravity of operator extended mass alo>>I, x axis, in..
Yo I!cccntrici ty of" center of pravity of operator extcndcd Illass along y ax1sq 1no Iiccentricity of. c.enter of gravity. of operator extended mass a10ng axis~ lno
, Bending 'section modulus of bottom bonnet velds, in 3 Z2
~
.Bonding> section modulus oi top bonnet Melds, in Z Torsional section modulus, oi .bottom bonnet welds, in Z4 Torsional s'ection modulus of top bonnet iields, in 3 E Z
7 Distance to edge of disc hub,. inches
). Maximum deflection of component, inches
<<13-
h 30 ANALYSIS NOMENCLATURE s(1) Combined bending stress in disc, psi S(2) Bending stress in disc due to bending along the shaft, psi S(3) Bending stress in disc due to bending about"the shaft, ps1 s(4) Bending tensile stress 'in unsupported flat plate; PS1 s(s) Shear 'tear out of shaft 'through disc, psi
. 'S(6) Sh'ear stress across structural hub welds of disc, pS1 S(7) Combined stress in shaft, psi S(8) Combined bending .stress in shaft, psi
'(9) Combined shear stvess 'in shaft, psi s(lo) Bending stress .in shaft due to seismic and pressure loads along x axis, psi S(11) Bending stress in shaft due to seismic load along
~
V GX15 PS1 S(12) Torsional shear stress in top shaft due to operating torque, psi S(15) Direct'hear stress in shaft due to seismic and pressure loads, psi I
S(14) Torsional shear stress at reduced disc pin cross-secti.on, psi S (15) Shear stress across top disc pin due to operating torque, psi S (16.) Bearing stress on top d'isc pin, psi S(17) Combined shear stress across bottom disc pin, psi (13') Shear stress across bottom disc pin due to torsional load, psi s(lo) Shear stress across bottom disc pin due to seismic load, psi
30 ANALYSIS NOMENCLATURE S(20) Compressive stress on shaft bearing duo to seismic and pressure loads, psi S(Zl). Shear tear out of cover cap bolts through tapped holes in bottom trunnion, psi I
S(22) Shear tear out of cover cap bolt head through bottom cover cap, psi S(23) .Combined stress in cover. cap bolts, psi I
S(24) Direct tensile stress in cover cap bolts, 'psi S(25) Shear 'stress in cover 'cap bolts due'o torsional loads, psi S (26) Combined stress in cover cap, psi S(27) Radial str'ess in cover cap, ps'i S(28) Tangential stress in .cover cap., psi
'S(29) Shear stress in'over cap,,psi S(30) Bearing s'tress on thrust collar, psi S(3l) Shear load on thrust, collar spring pin, pounds S(32) .Bearing stress of spring pin on thrust colla'r, psi S (33) Shear tear out of 'spring pin- through thrust collar, PS1 S(34) Shear tear 'out of spring pin through bottom shaft, p.s 1 S(35) Shear tear out of trunnion bolt through tapped hole in trunnion, psi S.(36) Bearing stress'f trunnion bolt on tapped hole .in trunnion, psi
. S(37.) Bearing stress of trunnion bolt on through hole in bonnet plate, psi S(38) Shear tear out of. trunnion bolt head through bonnet plate, psi S(39) .Combined stress in trunnion bolt, psi
ANALYSIS NOi~fENCLATURE S(40) Direct tensile stress in trunnion bolt, psi S(41) Tensile stress in trunnion bolt due to bending moment, psi S(42) Direct shear s'tress in trunnion bolt, psi S(43) Shear stress in trunnion bolt due to torsional load, psi S(44) Shear tear. out of operator bolt head through hole in bonnet, psi' S(45) Bearing stress of operator bolt on through hole in bonnet, psi S(46) Combined .stress in operator bolts, ps i S(47) Direct tensile stress in operator bolts, psi S(4S) Tensile stress in operator bolts due to bending moment, ps',
S(49) Direct shear stress in operator bolts, psi S(50) Shear stress in'perator bolts due to torsional .
loads,"psi S(51) Combined'stress in bo'nnet body, psi S(52) Direct tensile stress. in bonnet body,'psi S(53) .Tensile. stress in bonnet body. due to bending'moment, ps1 S(54) Direct shear stress in bonnet body, psi S(55) ,
Shea'r stres's in bonnet body .due to torsional load, psl S(56) Combined shear stress in bottom bonnet weld, psi S(57) Total tensile stress in bottom bonnet weld,-psi S(58) Direct tensile stress in bottom bonnet weld, psi S'(59) Tensile stress in, bottom bonnet weld due to bending
.moment, psi I
ANALYSIS NOMEiVCLATURE S (60) Total shear stress in bottom bonnet weld, psi'irect S(61) shear stress in bottom. bonnet weld, psi S(62) Shear stress in bottom bonnet <<eld due to torsional load, psi S(6S) Combined shear stress in'op bonnet weld, psi
\
S(64) .Total tensile stress in top bonnet weld, psi 1
S(65) .Dj.rect tensile stress "in t'op bonnet weld, psi 1
S(66) Tensile stress in'op bonnet weld due to bending moment, psi Total- shear stress in top bonnet weld, psi
'(67)
S(68) Direct shear stress in top bonnet weld, psi
'S (69) Shear stress in top bonnet weld due to torsional load~ ps1 ~
~
S(70). Combined stress in trunnion body, psi.
S(7l) Direct tensile .stress in trunnion body, psi S(72) Tensile stress in trunnion body due to bending, moment, psi S(7S) Direct shear stress in trunnion body, psi S(74) Shear stress in trunnion body due to torsional load; psi E
I
30
SUMMARY
TABLE INTRODUCTION In the following pages, the. pertinent'ata for, the butter-fly valve stress analysis is tabulated .in three categories:
'. Stress Levels for Valve Components
- 2. Natural Frequencies of Components
- 3. Valve Dim'ensional Data L
In Table 1, Stress Levels for Valve Components, the following data is 'tabulated:
Component Name Code Reference (when applicable)
Stress Level Name and Symbol Analysis'eference Page h/aterial Specification Actual Stress Level Allowable Stress Level The material.'specifications are taken from Section II of the code when applicable. Allowable stress'evels are Sm for tensile stresses and'6 Sm for shear stresses. The allowable levels are the same whether the calculated stress is a combined stress or results from a single load condition. Sm .is the design stress intensity value as defined in Appendix I, Tables I- 7. 1 of Section III of the code .
In Table 2, Natural Frequencies of Valve Components, the following 'data is tabulated:
30
, Summar Table Introduction Component iVamc Natural Frequency Symbol
'Reference I'nalysis Page f
Component i~latorial Natural Frequenc>
'n, Table 3,'Valve Dimensional Data, the values 'for the pertinent valve dimensions and parameters are gii'en.
4
Table 1 STRESS LEVELS I'OR VALVE COMPONENTS Allowable'tress
.Code Ref. Ref. Stress Level Component Paragraph Name 4 Symbol Page Material Level; psi ps I.
f I
Body NB-3541.1 Primary membrane Pm AStlE SA-516 Gr.S5 Sm stress in. crotch Ic "I+ 13700 re ion Primary membrane
'Pm'5 .ASME SA-516 Gr.55 Sm t
I 13700 NB-3545.2 Primary plus secon- 36 ASME SA-516 Gr.55 Sm dary stress duc to Qp g790 13700 internal rcssure I NB-3545. 2 Pipe reaction Stress Axial Load Ped 36 ASME SA-516 Gr.55 I}8& 1.5 Sm 20550 Bending Load . Peb 36
.T'orsional Load 36 P. 594-.
NB-3545. 2 Thermal Sccondarg qt . 38 " ASMH SA-516 Gr.SS i@5 Sm J
St1 css ~
137no NB-3545.2 Primary plus secon- Sn 38'SME SA-516 Gr'.55 7~9$ 3 Sm dar stress 41100 NB-3543. 3 Normal duty fatigue Sp 38 ASME SA-516 Gr. 55 stress Na + 2000 65nnn Disc HB-3546.2 Combined bending S(1) 39 ASMH SA-516 &9)+ 1.5 Sm stress in disc 2ffssn NB-3546.2 Bending tensile in .
S(4> 41 ASME SA-516 Gr'.70 80J5 Sm unsupported flat I 17500 C7 late I
i STRESS LEVELS i'OR VALVE COMPONENTS Al1 o>>'ah 1 e Code Ref. Ref. Stress Stress Leva Component Paragraph Name P Symbol Page Material Level, psi ps1 Disc, NB-3546.2 Shear tear out of S(5) 41 ASME SA-516 Gr.55 7) lh .6 Sm Con't. shaft thru disc 8220 Shear stress across S(6) 41 yQ.5+ .6 Sm di'sc hub welds 7220 Shafts 'NB-3546.3 Combined stress in S(7) 42. ASME SA-.564 Type ~k lo+ Sm shaft 630, Cond. H-1150 33700 NB-3546.3 Torsional shear S(14) 43 ASh1E SA-564 Type .6 Sm stress at reduced 630, Cond.'l-llSO 20220 in cross-section Disc Pin NB-3546.3 Shear stress. in ', S (15) 44 AShlE SA-320 Gr.BBM .9 x yield to in .
27000
.9 x yield NB-3546. 3 Bearing stress on S(16) AShIE. SA-320 Gr. B851 )3 27000 to i in I ~
NB-3546. 3 Combined shear S(17) 44 'ASME SA-320 Gr.B8M .9 x yield stress in bottom la~8 27000 I
)ln I
Shaft Compressive stress S(20) 45 AS'I'i~l 13-438, Gr.1 ,Psg74 Sm Bearin on shaft bcarin 'I'ypc lI 13ron e 4000 Cover Cap NB-3546.1. Sh'car tear out of. S(21) 46 ASIlE SA-516 Gr.55 .6 Sm cover cap bolts ) 7A9 8220 thru t~l>pcd holes.
in bottom trunni'.on NB-3546.1 Shear tear out of S(22) 46 ASME SA-516 Gr.70 .6 Sim cover cap bolt- head 10500 thru cover ca
STRESS LEVELS FOR VALVE COMPONENTS Allowable Stress Code Ref .. Ref. Stress -Level,
'Component Paragraph Name 4 Symbol Page Material, psi
'evel, psl Cover Cap NB- 3.54'6.; 1 Combined stress .in S (23) 46 ASME SA-193 Gr. B'7 Sm (con't.) cover'ap bolts J b9'7 25000 Combined stress in S(Z6) 46 ASME SA-516 Gr. 70 Sm cover cap 17500 Thrust " Bearing stress on S(30) 49 SAE-660 .9 x yield Bearing thrust collar. ) l 0+ 14400 ~ ~
Shear load on thrust collar S(31) 49 . 'AISI-420 D9-5+ .Pm spring pin Bearing stress of .9 x yield s~iring pin on 14400 thrust collar S (32) 49 SAE-660 )ol88 Shear tear out af.
spring pin thru S(34) 49 ASME SA-564 Type .6 Sm bottom shaEt Cond. H-1150 '30, 20220 Operator Shear tear out of Mounting trunnion bolt thru S(35) 50 ASME SA-516 Gr. 55 .6 Sm tapped hole in 8220 trunnion.
Bearing stress of Sm trunnion bolt on S(36) 50 ASME SA-516 Gr. 55 Rot'o 13-.no tapped hole
.0
.STRESS LEVELS POR VALVE COMPONENTS lofti I
I Al able Co'de Ref. Ref. Stress Stress Leve Component Paragraph . Name 4 Symbol Page Material, Level, psi psi Operator Bearing stress of, S(37) 50 ASh1H SA-36 hIounting, trunnion bolt o>> j 0740 Sm 13700 Con't. thru hole in bonnet Shear tear out of s(38) so ASME SA-36 .6 Sm trunnion bolt head g ~ah 7500 thru bonnet Combined trunnion holt stress in S(39) '2 ASTM SA-193, I'r.B7. 3So8 .9 x 94500 yield Shear tear out of S(44) 52 AShlE SA-36 0 Slil ope'rator bolt head 7560 thru hole in. bonnet Bearing stress s(4s) 52 AShIE SA-36 Sm
.bolt hole in bonnet on of'perator I 69ii 1'000 Combined stress in S(46) . 52 )8o9'4 Sm o )era tor bolt AS'I'.I SA- I 93, Gr. II7 'nu.i
.9 x yield Combined stress in' s(sl) ss AShIE SA-36 > 04-8 32400 Combined shear s(s6) s6 .6 Sm stress in bottom . '00 bo>>nct fields Combined shear S(63) 56 .6 Sm
~ stress in top )>13 ". '00 bonnet i~elds Combined stress in S(70) 57. ASME SA-S16 Gr.ss 175) Sm trunnion bod I .=.. il<<
~ ~
l ~
\
TabIe 2 NATURAL PRBQUENCIBS OF. YALVH COMPONENTS Natural Natural Component Frequency Re f. Frequency Name Symbol Page Material (Hertz) .
Bogy FN1 58 ASi~EE:..SA-516 Gr.55 Banjo FNZ AStlL'A-564 Type 630 Cond.. Il-1150 Cover Cap FN3 59 AsnEE:. SA-516 Gr.. 70 A-36i Bonnet FN4 60 AST>E
+82 I
I '~
I I
Job Number:
Operator Mounting: 'Operator: )k--S Cg A C0 Gb Cy A4 ,i5G C8 GT ~5 C9 gx A'0
'y Ez As H2 By DZ id Hg
.B2 Dp Bg D4 ~
Hg
.J .'4 Dg Bg D0 Hy B0 Dy HS
'By H9.
B8 B9 Z2 M'7 j ~
~
C Cb Z4 ad ~ '7
" Co 1,63 a. k.SV Z0
'2 0 Sc Iy
~ ~ \
~ '25
M 4'T2 z
T2 J4 M T3 J5 "v T4 T5 Ko OQP K1 N1 T7 K2 N2 TS K3 .b..<o N3 U1 UZ U3 Ps Vj Ly V2 Lp Y3'4 L3 L4 V5 R4 V6 L6 V7 L7 Vs LS R6 W1 1. ~.5 Lg 9'1 7 W3 tm 26
Zo Zg C
Z2 Z3 o Z4 Z7 M
26a
P Pages 20-26, Stress Level Summary sheets, Frequency Analysis
.Su@ma'ry shoots, and Valve Dimensional Data sheets have 'been assembled at. ihc beginning of -the report submittal. They are located directly. behind'he design review record for the corres-ponding production order.
20-26
Standard Stress Report.
for .
NRS Butterfly. Valve w'i th Bonnet Mounted.
Cylind'er Operator 30 ANALYSIS INTRODUCTION Described in the following pages is the analysis used in verif> ing the structural adequ'acy of'he main elements of the NRS, butterfly.'valve. The analysis is structured to comply with Paragraph blB-3550 of Section III of the ASllE Boiler and Pressure Vessel Code (hereafter referred to as the code) . In I
the analysis, the design rules for Class' valves are used, since the requirements for,this class of valve is much more
~
explicit, than for either Class 2 or 3 design rules. The de-sign rules for Class 2 and 3 are'exceeded by the rules for
~
Class 1 valves.
Valve components are analyzed under the assumption that the valve is either at maximum fluid dynamic torque or seating against the, maximum design pressure. Analysis temperature is 300 0 F.'eismic accelerations are simultaneously applied
.in each of three mutually. perpendicular directions.
Seismic loads are'made an integral part of the analysis by the inclusion of the acceleration constants gx, gy, gz.
Thc symbols gx gy gz represent accelerations in the x, y and z directions respe'ctively. . These directions are defined with respect to the valve body centered co-ordinate system's illus-tratod in Figure l. Specifically, the x axis is along the pipe axi's, the z;axis is along. the shaft .axis, and'he y axis is mute~all>~ perpendicular to the. x and. z axes, forming a right hand tri.~d with them.
~
Figure 1 VALVE BODY Si'ATIAI. ORIENTATION Anal s is I n t rodu c t i on Va lvc o rie n t a t.i on w i th respect t o gravity is taken i n t o account by adding the appropriate quantity t o the .seismic 1 oads . Th o justification for do in g th i.s is that a g rav i-t a t i o n a 1 l oa d is c omp 1 e t e. ly cqu i va 1 en t t o a 1'g seismic load .
'he analysis'f each main element .or sub-.assembly of. the butterfly valve is described separately in .an appropriately titled 'section. In addition to containing sketches where appropriate, each section contains an explanation of the basis for each calculation. 1'/here applicable, it also contains an interpretation of code requirements'as they apply to the analysis.
Figure 2 is a 'cross'-section view of the butterfly valve, and its associated'omponents. Detailed sketgpe's are provided
'hroughout the .report to clearly define the geometry.
~ I 30
- TOP SHAFT SHAFT PACKING
.SHAFT BEARING TOP TRUNNION VALVE SEAT DISC PINS DISC
'BOTTOM SIIAFT BOTTOi~) TRUNNION COVER CAP Figure 2 VALVF t ROSS SFCTTON
END CONNECTION ANALYSIS Thc NRS butterfly valve is a uniflange design. Rather than having flanges that are external to and.distinct from the body, the bod> shell is fabricated so that the end connections're machined directly into the body shell. The outside and inside diameter of the 'body shell conform to the requirements o'f the American National. Standards 'Institute (AN'SI) st'andard 816.5. The end'connections, either .flanged or iield end, also conform to this standard.
4
/~g $
I
'BODY ANALYSIS The body analysis consists of calculations as detailed in Paragraph NB-3540 of Section III of the Code. Paragraph NB-3540 is not highly oriented to butterfly valves as related to, various design and, shape rules. Therefore, certain of the design. equations cannot be directly applied for butterfly valves. Where interpretation unique to the calculation is necessary,'t is explained in the subsection containing that
~ 'calculation description.
Figure 3 illustrates the essential features of the body geometry through the trunnion area of the valve. The symbols used .to define specific dimensions are consistent with those used in the analysis and with the nomenclature used in the Code..
- 1. Minimum Body Wall Thickness Paragraph NB-3542 gives minimum body wall thickness'e-quirements for standard pressure rated valves.
4 The actual minimum wall thickness.in the NRS valve occurs between the'lange bolt holes and body bore.
PRESStJRE -ARE >Y 'ANALYSIS BODY CROSS-SECTION Figure 3
30 Bod Analvs is
~
- 2. Body Sha c Rules The NRS valve meets the requirements of Paragraph NB-'3544 oE the code for body shap~ rules. Th'e ex-ternal Eillot at trunnion to body intersection must be greater than thirty percent of the minimum body wall. thickness. ~
- 3. Primar Membrane Stress Due to Internal .Pressure Paragraph NB-3545.1 .defines the maximum allowable st'ress in the neck to flow passage junction. In a butterfly valve, this corresponds with the. trunnion to body shell junction. Figure 3 shows the geometry through this sect'ion.
The code defines the stresses in'his area using the pressure area method. As seen in Figure 3, certain code-defined dimensions are not applicable to this style of butterfly valve. For example, there is no radius at. the crotch when seen in a view along the fl'ow pattern, as the neck exten'ds to the face of the body. To comply'ith the inTent af the code, the areas AE and Am are interpreted as shown in the cross-section -(Figure 3). Using these areas, the primary membrane stress is thon c'alculated.
Pm = ~AF/Am+ f 5) Ps 30 As an alternate method of determining the primary membrane stress, an equivalent analysis for primary membrane stress is applied to an area away from the triinnions. In .these areas, the met'al area and fluid area aro as shown in Figure 4.. Since the depth of the metal area is equal to 'the depth oS the fluid .area, the ratio A'f/Am is equivalent to the mean radius of the body over the thickness of the body shell, Rm/H9.
.The primary membrane stress through this section is then:
Pm) = (Rm/H9+.5) Ps Secondar Stresses A. Body Primary plus secondary stress due to internal pressure'Paragraph NB-3545.2(a) of Section III
~
of the code defines the formulas used in calculating this stress.
Qp Cp ri + ' ps
.B.. Secondary stress. due to pipe reaction: Paragraph NB-354$ .2(b) gives the formulas for finding stress due to pipe reaction.
Ped = FdS (Direct or Axial Load Effect)
Gg Pgb, = CpF>S (Bonding Load Effect)
Gb (T'orsional Load Effect)
- 36-
30 Hg r k A PRESSURE AREA ANALYSIS CROSS-SECTION IN BODY" Figure 4
30 Bod Anal sis V
C. Thermal secondary stress: Paragraph NB-3545.2t'c) of Section III of the code gi'ves formulas for
,dctcrmining the thermal secondary stresses, in the pipe.
=
QT QT1 + QT2 lUhere QT2 = C6C2LT2 D. Primary plus .secondary stresses: .This calculation is per Paragraph 'iilB-3545.2 and is simply the I
'um I of the three previous secondary stresses.
Sn. = Qp + Pe + 2Qtz 3S
/
A Valve Fatigue Re uirements NB-3543.3 of Section 'aragraph III of the code de'fines-requirements for normal duty. valve fatigue.
allowable stress level is found from Figure I'he I-9.0. Since the number of cycles is unkno4'n,.a maximum value of 2,000 is assumed. The allo)cable stress can then b'e found from Figure I-9.1 for carbon'teel. This then gives an allowable stress of 65,000 psi.
-Spl = 2/3 Qp + Peb/2 + QT3 + 1 3QT1, Sp2 '4 Qp
+ 'Peb + 2QT3 lUh ere:
QT3 = C6C3hTZ
-3S-
5
- 30 DISC ANALYSIS
~ Section NH-3546. 2 defines the desi.gn requirements of the valve disc. Both primary bending and primary membrane stress are. mentioned in this section. For a flat plate'u'ch as the butter'fly valve disc, membrane stress is not defined until the deflection of the disc reaches one'-half the disc -thickness.
Since total deflection of the disc is much less tha'n one-half the thicl'ness, membrane stresses are not applicable to the analys.is.
Figure 5 shows the disc for the MRS butterfly valves.
..The disc i.s designed to provide a structurally sound pressure retaining compo'nent while providing the least interference to the flo>> .
Primary Bendin Stress N
Due to the manner in which the disc is supported, the disc experiences bonding both along the 'shaft axis and about 'the shaft axis. The combined bending stress i's m'aximized at the disc center where, the maxim'um moment occurs. The moment is a result of a un.iform pressure 1oad.
Combined bending stress in disc:
S('1) =. (S(2) + S(3) )~
.1Uhere S(2) = .90413 PsR,) C7 Bending stress due to moment along shaft axis, psi Ig S(3) = .6666 PsR j C8 Bending stress about.
due to shaft axis, psi moment
'30 DISC PINS SHAFT BORE UB BLOCK IIUB lllELDE SEAT
~FLAT PLATE RETAINER SCREli'S NRS VALVE DISC
~
Figure 5
Disc Anal sis Bending stress of unsupported flat plate:
S(4) ~ MgCg
~7 Shear Tear Out of Shaft The disc is designed so the minimum thickness of material surrounding the shaft extension in the disc is above the shaft on the 'arch side. The loading is. due to;both seismic and pres'sure loads.
S.(S) - s 4 2 +
g'g'+g' = Shear tear out shaft 2L9{K2,+3) 9 2' (1-SyN 45 )) through disc, psi .
Shear Stress in Hub Nelds s(s) -. 2 R4 Ps + T8 ~R42 28'g 2+g 2) < 2 N6Lg 271f6L6 LgNg
~
~
41
30
.SHAFT ANALYSIS'he shaft is analyzed in accordance.wi:th Para NB-.3546.3 of Section III of the Code. The shaft loa'ding is a combination of seismic, pressure, and operating loads. Maximum torsional 5
loading is either a combination of seating a'nd bearing torque or bearing~ and dynamic torque. Columnar stress in not con-qidered in the shaft loading due to its'egligible effect on the stress levels. Figure 2 shows the banjo'ssembly with the through shaft,.
Shaft stresses due to pressure, seismic and operating loads:
Nh,ere:
S(8) = (S(10)'2+S(11)2)< =. Combined bending stress; psi S(10) = (>R42Ps+N2gx).25 BIR5' Bending tensile stress m'25R m.25R5 4 due to pressure and seismic loads along x axis, psi d(al) = 25N2 gv B1R5 = Bending tensile 'stress
. 25 "m R54
. due.to seismic loads along y axis, psi S(~) (S(12) 2+S(13) 2) g ="Combined shear stress, psi S (12) Torsional Shear st'ress, ps.i
. 5>R54 S(13) 1+333 5>R42ps+ 5N2(gx2+gv2)"- Direct shear mR5 stress, psi Also worthy of at tention is the torsional shear stress at the reduced cross-section where the'isc pin passes through the shaf t i J ~
30 Shaft Analysis'(14) mR~4
= 'S(12)
>Rg" - DpDp - DjDp 2 12'12
DISC PIN ANALYSIS
's seen in Figure 2, there are two stub shafts to the disc pins. The top pins are subjected to torsional load as they transmit the operating torque. The bottom pin is subject to shear loads due to seismic and torsional loads.
Shear stress in top disc pin:
S(15) = '8-. SU5 2N1R5.785D3 Bearing stress on top disc pin:
S(1l.) = T,-.SU 5 .
2RSK2D3N1 Combined shear stress - bottom disc pin:
S(17) = S(18) +S(19 )
Torsional shear stress in bottom disc pin:
S(18) ~ (.SU5+U6) 92 '85D3
~
~
Shear stress in bottom pin one to seismic accelerations
+ pressure 'on end of shaft:
S( .19) = M2g +~R5 2 P 2 z 5 0 2 (. 785) D3
~ ~
44
P DISC PIN ANALYSIS >
~
Nhere:
2 U4 =- . 785 (2R4) P0U3R5 U5 = U4 + N2g U3R5 U6 = W2g + mR5 2 P .25(D4 +D2 2 z P
0
= Actual shut-off pressure F
44a
SHAFT BEARING ANAI.YSIS
'I The sleeve bearings in the trunnion (Figure 2) are subjected to both seismic and pressure,load's.
S(20) = >pdR42+h'2(gx2~g 2)4 Compressive stress on 2 LSDZ shaft bearing, psi
~ (
~, I COVER CAP ANALYSIS ~q ~
Figure 6 shows the bottom trunnion assembly, including the cover cap and cover cap bolts..
- l. Cover cap bolt stresses:
The cover'cap experiences loading from the weight of the banjo and from pressure loads: In determining stress levels, the bolts are assumed to share torsional and tens'ile loading equally.
Shear tear out of bolts through tapped holes in trunnion:
2 S4 21~ Nz gx +g 2
+gz 2 + ""Ps 'R6 2 4 L3 2.83-D6
- Shear tear out of bolt heads through cover cap,'psi:
S( 22) 2 2 ~ 2 + + Ps R 2 Mz x +gy +gz 4 Tl S.2 D6
-.Combined stress in bolts, psi:
$ (23) S(25) + ( S(25) + .4S I,24) )
2 2
~
Mhere:
S(Z4) - .2S Nz g x.2+g y 2+g z'2 (D2 + .66 (D4 Dz~~
707 H3 4 A4
~ Shear Stress in Bolts Due to Torsional Load.
46
s ~ ~
MS- ~ ~
i~
g ~
k ~ ~
. ~
Cover Ca Anal sis S(25) N2 g~ +gy +g + Ps R62 Tensil'e Stress in Bolts 4 A3. Due to Seismic And Pr'essure Loads, psi
- 2. Cover cap stresses:
The combined stress in the covercap is calculated using the follow-ing formulas:
S(26) = S(2") + S(28) + ((S(27) + S(28)) + 4S(29) )~
2 2 Nhere: r S(27) ~ 3(.785 (D4 + .25) Ps + ~~2gz)
= Radial Stress T42
- Il S(28) 3(.785(D4 + .25) s
+ N2gz) Tangential Stress 4 .~ T42m.
A S(29) ~ .785 (D4 + .25) Ps + N2gz
= Shear Stress (D4 + .25) T4 48
THRUST BEARING ANALYSIS As seen in figure 6, the thrust bearing assembly is located in the bottom trunnion. Xt provides restraint for the banjo in the z direction, assuring that the disc edge remains correctly'osition-ed to maintain optimum sealing. Formulas used to analyze the I
1 assembly are'iven below.
- 1. Bearing stress on thrust collar due to seismic and pressure loads:
S(3'0) ~N2 x 2+e 2+g 2 gy z
~ x Ps R2 5
..185 (D4 - (D2+. 25) )
- 2. Shear load on thrust'ollar spring pin due to seismic, pres-sure and torsional loads:
S(31) (N2gz+ " s R5 )
+ .25 N2gz(D2+.0833+.66 (D4-D2))
R5 3 Bearing stress of spring pin on thrust collar:
((N2gz+ " s- R 2)2 + (.25 N2gz)
D5 (D4-D2)
- 4. Shear. tear out of spring pin through bottom of shaft:
~ W2g 2 S(34) + <<P RS
~
'.2D2 V2 49
1 OPERATOR MOUNTING ANALYSIS The operator mounting consists of the top trunnion, the bonnet, the operator housing, and the bolt connections. The elements of the assembly are. shown in Figure 7.
- 1. Bolt stresses and localized'stress due to bolt loads. The following assumptions are used in the development of the equa-tions:
A. Torsional, direct shear, and direct tensile loads are shared equally by all bolts in the pattern.
. Moments across the bolt pattern are opposed in such
.a way that the load in each bolt is proportional to its
=distance .from the neutral bending axis.
(a) Shear tear out of trunnion bolt through tapped hole in top
<runnion.
Q (g2) ~ F +P z 4 g x 2+g 2~g z 2 y Nx( p') N ( g')
2J2 +2(~2+H2) 2Jl +2(~1+H2)
-' L4D7 (b) Bearing stress on tapped holes in trunnion.
SPS) + T 8 (F x +Fy ) N4 (g x +g y )
+
4(. 707 H2) 4 4 D7L4 (c) Bearing stress on through hole in bonnet.
S (34) M T88 (F x 2+F y 2)< N4
~
4 (g x 2+g y 2)~
~
4(;707 HZ)
' '4 D7T6
~
~
0 erator Mountin Anal sis (con't.')
'(d) 'hear S(35) = Fq+H45q 4
'x tear out. of trunnion bolt 2J (J3+H3)
+3 (J3+H3) heads through bonnet.
M (Jl+H2) l'"Z) 5.2 D7T6
'0a
30 TOP TRUNNION h10UNTING FIGURE 7 Qo
~ ~
FILLET 4'ELD
~ \ ALL AROUND
~
~~
5 ~
>it. /'
~ ~
i!i
~
o
~
>>i, >,1 ~
~
'>)f
>I>~ ~
i BONNET TOP TRUNNION YALVE l30DY TRUNNION BOLTS
30 1
~
0 crator hlount1ng Allal s1s e.. Combined stress in trunnion bolts (See Fig. 8)
S (i9)' S (40)+S (41) + ( (S (40)+S f 41))2+4 (S (42)+S (43) ) ) ~
? 2 Yhcrc S (40) F.+144g, = Direct tensile stress PSl 4A5 S(41) I'ix (J2+H2) R (Jl+H2) Tensile stress due to extended 2J2 +2(J2+H2) 2J1 +2(Jl+H2)- mass bending A5 moment, psi S(42) (Fx +F 2) "- + N4 (gx2+ q 2) ~. Direct shear 4Ag'. stress, p'si S.(43) = (ht,+T8) = .Shear stress due
( ~ 707 HZ) 4A6 to torsional load, PS1
- f. Shear tear out of operator bolt"head through bonnet.
S(44) = r-. +. Mxv6' V8W 5.2 D8T7
- g. Bearing stress on through holes in bonnet.
S(45) hlz+18 + (F<2+Fv2)
.5 H7N2 N2 D8T7
- h. Combined stress in operator bolts (See Fig. 9)
S(46) = S(47)+S(48) + ((S(47 +S(48) ) 2+4 (S(49)+S(50) ) 2)'
b'herc
'(47) = F-N2A7
30 F12 FT2" K4 TOP TRUNNION BOLTING 3'igure 8
30 OPERATOR BOLT PATTERN Figure 9
0 erator Mountin Anal sis S(48) = Md'6 5+6 7
+>>8 7S7 S(49) = (Fx2 F 2)
"z s M+T H7N2A8
that loading is through the bolt connections as previously defined.
- a. 'he maximum combined stress in the bonnet was calculated using the following formulas:
s(sl) = s(sz)+s(ss) ((s(sz)+s(ss)) +a(s(sa)+s(ss))
Combined stress in bonnet legs S(52) F +Wag Direct tensile stress, psi 5
S(53) = M Ba + H B9 l 2, = Tensile stress psi dne to bending moment, S(54) = (F +F )" + W (g +g ) = Direct shear stress, psi 5
S(55) = T Co = Shear stress in bonnet body due -to torsional Ko load, psi where T
Torque, in-lbs.
Co = Torsional constant for non-circular cross-section Ke
%I Function of cross-section, in.a
- b. The maximum combined shear stress in the bonnet mounting plate to body welds was calculated using the following formulas:
0 erator Mountin Anal sis'ottom Bonnet Weld S(56) S(57)+4S(58) 2 ~ ~ Combined shear stress in bottom veld, psi Where S(57) = S(59)+S(60) ~ Total tensile stress, psi S(59) =. Fz+W4gz ~ Direct tensile
.Ul stress, psi S(60) = M + hg ~ Bending tensile 1,2 stress S(58) = S(61)+S(62) Total shear stress S(61)= (Fx'F )> + W4 (gx2+gy2)4 Direct shear Ul stress, psi S(62) ~ Mz+T8 ~ Torsional shear Z3 stress, psi Top Bonnet Weld S(63) = (S(64 2+4S(65) 2)< ~ Combined shear 2 .stress in top bonnet veld Where S(64) ~ S(66)+S(67) ~ Total tensile stress, psi S(66) = F, ~ Direct tensile Qg stress, psi S(67) ~ Mx M ~ Bending tensile stress, psi.
~
S(65) = S(68)+S(69) ~ Direct shear stress, psi
30 0 orator i~tountin Ana.l sis Di.rect'hear stress, psi S(69) = M +TB = Torsional shear'stress, psi Z4
- c. Trunnion body stresses are calculated 'ising the iollowing assumptions:
1.,Operator 'leading is through the bolt connections.
2; There is. an equal and opposite reaction:to the bolt .loads at the body.
.The combined stress'in. the trunnion body >>as calculated using the folio>>ing formulas:
S(70). = S(71)+S(72 + ((S(71)+S(72'))2+4(S 73)+S(74 2)~
1)here S(71) = Fz+N4gz Direct'ensile stress, psi K4KS-.785 BBZ 1
S(72) (hlx+F K6) 5K4~ + (M +FxK6').5K5, = Bending tensile
.0833K5K4~->B)4 4K53 B24 stress, psi 64 64, S(73) (F - +F )" + t<4(g +g )< = Direct shear K4K5-.785 B2 stress, psi S(74) = (i~l~+T8) ' (K42+K52) lg = Torsional shear
~ . 0833 (K4K5 +K5K4~) -ii'B2" stress, psi
~3
- 5 7.-
50 C *
- A. Introduction To calculate the natural'requency'f. the various components oE'the Nl
>ei,ght, in.
E I5 C. Banjo Assembly Figurc 2 sho>>s. thc banjo assembly. in thc body. The natural frequency of thc banjo assembly is calculated using the foll'owing:
~
N2 Where
- ly2 = N7B1 = hlaximum deflection of.
12 E IG shaft, inches D. Cover Ca Assembly As seen in Figure G,,the cover cap supports the banjo.
The natural frequency of the cover cap is -calculated as folio>>s:
9.8 '-'v llherc
~) 5 5 (m2- 1 ) N2 r
(; 51)4+ .'1 2 5) ', = hlaximum def lection 16 n: -
r- 'I' 4m"
. Of cover cap .
E.-,Bonnet Assembly e
Figurc 7 shows thc top trunnion assembly. The following assumptions are made in calculating the bonnet natural frequency; 30 I'rc ucncv Analysis l.'I'he worst valve assembly mounting position is where
~
the bending moment is predominant in producing de-flection.'.
Thc bonnet is assumed fixed at the top trunnion..
- 5. The adapter plate is assumed to be integral with and have a cross-section the same as the component it
~
mounts to.
Natural frequency of bonnet:
-" 9.
Fn4 S 4'he re
~y4 = N~H8 +44K-, + NgZoHg
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Qo POSITTOM 3 l X Oo F=NO.AND SIZE OF HQf ES X Pos/rlotU P t E'EEP/ STRADDLE CENTERLINE B- -.'. 150LB USAS FLANGE BOLT LAYOUT.
I-1 (-7(
REV.- DATE BY APP. I kw.->-7C REV.-DATE APP.
tli'- II-',"N1< ]f'ENRYAUttCtRA. PRATT COMPANY GENERAL ARRANGEMENT AS, .I:
P, ERT.V,FlE NUCLEAR N-R.S. VALVE t'I SPRING RETURN OPER-W/BON.'ETTIS
.. NPT. BLEED-OFF CONNECTION FLANGE X WELD END ICI'OMINAL 2 NO NE 5-2 (CAPP ED W/P. IP E PLUG). scA DATE 8-74'RAWN VALVE SIZE BY ' 'CHECKED BY DD= R.F, DIA.. t APPRDVED / "s rt G=BOLT CIP'CLE 1! ~
POSI TIOil .q PA>> ND D-0026-l P OS( TIOQ 2 C
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/ .f PARTS AND MATERIALS OF,CONSTRUCTION , PARTS AND MATERIALS OR CONSTRUC,IION r
I. BODY: MAT'L.Y SA-5I6 GR.- 55 t
' I I. THRUST, COLLAR PIN: MAT'LA AISI 420 STN. STL IH
~
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- 2. SEATING SURFACE: MAT'L.Y SA-479 TYPE 304 r2. GREASE: DOW CORNING III.
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DISC: O-,RING: MAT'L; E.P. T.
I
'3A. HUB: MATtL.g SA-5I6 GR. 5S SA-5lb r
BOTTOM COVER: MAT.'L.o I GR. 70 l I r
.38. FLAT PLATE: MAT(L.I SA-ID 16 GR.70 I5. COVER BOLTS-'AT(L.e'A-!93 GR. 8-7 SEAT: MAT'L.; E.P. T. I6. LOCKWASHER: MAT'L; CARBON STEEL CLAMP SEGMENT RING: MAT'L.> SA-285 GR. C 17. BOTTOM BEARING: MAT'L. ASTM B-438 GR.I TYPE 2 BRONZE I
ff I
I
- 7. SHAFT: MAT(Lg SA-564 TYPE 630 COND. HI I%0 !9. SHAFT SEAL: MAT'Lu E P.T.
- 8. PINS: MAT'L.; SA-320 GR. BBM 20. PACKING RETAINER RING: MAT(L.Y SB-144 ALLOY 3B
- 9. THRUST COLLAR SHIMS: MAT(L.> HARD BRASS 2I. PACKING: MAT'L.e E. P. T. V-RINGS
- 10. THRUST COLLAR: MAT'L.'AE 660 BRONZ 22. LANTERN GLAND RING - MAT'LyASIAN A-269, -
f I I
I I 7 STUB SHAFT COATED WITH SILICONE LUBRICANT
- , I I
FOR ASSEMBLY PURPOSES ONLY. 'I i
~-
NOTE:
I-PIN TOP & I%IN BOTTOM FOR l4>> VALVES.
2-PINS TOP & I-PIN BOTTOM FOR l6>>
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t BE PT>> EXAMINED DISC'HUB WELDS MILL BE ((PT>> PR) ';; PURPOSES ONLY.
>>MT>> EXAMINED.
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