'I

.i'REGULATORY ORHATION DISTRIBUTION SYS; (RODS)

AOCESSION„NBR;8203300)$ 8 , DOCRPATEt 8QP03/24 NQ'fARXZED: NO'FACIL~50 335 St-. Lucie P]anti„Unknit 1E Rior ida 'Power L Light Co.

'AUTH INANE AUTHOR AFFILIATION'UMR IG iR, E ~ Flojida ~Power,, 5 Light Co,

'R <C IP ~ I«l AH E RECIPIENT A F F IL"IA TIg NCLARK RE A, Operating Reactors Branch 3

DOCKET05000335

SUBJECT: For wards. Heor y;Pratt Co analysis of containment purgeisolation valves «per NRC 820223 request.l/'ISTRIBUTIONCODE: A0$ 0S iCOPIES >RECEIVEDiLTR +~ENCL J SIZE:.," -Z+

TI'TLE: Containment 'Purgirig

NOTES'ECIPIENTID CODE/NAME',

ORB P3 BC 01

INTERNAl: IE 06NRR SHUMiDNRR/DL/ORAB 10NRR/DS I/AEB

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,-COPIESLTTR ENCL

EXTERNAL: ACRSNRC PDRNTIS

1302

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0305

)TOTAL NUMBER OF COPIES, REQUIRED: L«TTR 33 ENCL 32

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FLORIDA POWER & LIGHT COMPANY

March 24, 1982L-82-115

Office of Nuclear Reactor RegulationAttention: Robert A. Clark, Chief

Operating Reactor Branch 83U.S. Nuclear Regulatory CommissionWashington, O.C. 20555

Oear Mr. Cl ar k:

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St . Luc ie Uni t 1

Oocket No. 50-335Pur in and Ventin of Containment

Enclosed is the Henry Pratt Company analysis of the St. Lucie Unit 1

containment purge isolation valves that you requested in your letter ofFebruary 23, 1982. The other items addressed in your letter are beingreviewed and will be responded to separately.

Very truly yours,

t E. UhrigVice PresidentAdvanced Systems and Technology

REU/PKG/mbd

Attachment

cc: Mr. James P. O'Reilly, Region IIHarold F. Reis, Esquire

S

( (

8203300i58 820323PDR ADGCK 05000335P PDR PEOPLE... SERVING PEOPLE

SUMMARY DATA

VALVE, SIZE AND TYPE: 48" R1A PRATT JOB NO.:D-027270-1 a 2

OPERATOR. T-520 SR-2 /Bettis

Vent & Purge Valves

Standard Calculation Pressure (Design Pressure) psig

Operating Pressure (Maximum) 39 psig

Acceleration Levels (Design)

3: gv

gZ

Acceleration Levels (Specified) gx

gZ

I

Specific Design -Pressure psig

, Minimum Valve Wall Thickness inches

Code Required Wall Thickness , inches

Form No. HPCo. 3. 173N- 8203300158

I. General Arrangement and Cross-Section Drawings

II.. Introduction

IXI. Considerations

IV. Method of Analysis

A. Torque Calculation

B. Valve Stress Analysis

C. Operator Evaluation

V. Conclusion

Attachment 1 Pressure vs. Time Graph

Attachment 2 Temperature vs. Time Graph

Attachment 3 48" NRlA Valve Stress Report

Attachment 4 Bettis Letter dated Hay 19, 1980

Attachment 5 Bettis Letter dated June 13, 1973

Attachment 6 Bettis Seismic Report

I'ENERAL ARRANGEMENT AND CROSS-SECTION DRAÃINGS

Page 1 of 7

~ re so owe J%81+s!Cff11 ~ 0 ~ ~ i ~ ~ ~

II. Introduction

This investigation has been made in 'response to

a request, by the Customer/Engineer for evaluation of

the 48" containment isolation/purge valves originallyfurnished on Pratt Order No. 7-4491-1 regarding

structural adequacy to withstand the dynamic torques

which would occur during a faulted condition of a loss\

of coolant accident (LOCA) within the containment vessel.

The valve assembly would be capable of closure during

this event in a time equal to or less than that ori-ginally specified. Containment- pressure-time data

was furnished by the Customer/Engineer to identify the

maximum differential pressure across the valve and to

identify fluid dynamic torque coefficients.. This is

included as. Attachments 1 and 2.

~ to so ~ ~ FWlla5fQCj

III. CONSIDERATIONS

NRC guidelines for demonstration of operability

of purge and vent valves, dated 9/27/79 has been incor-

porated in this evaluation as follows:

A. l. Valve closure time during a LOCA will be lessthan or equal to the no flow time demonstratedduring shop tests, since fluid dynanic effectstend to close a butterfly valve.

2. In this analysis we have considered the directionof flow furnished by owner which is the directionresulting in higher torque. We have used differ-ential pressure-time data furnished by owner.(See Attachments 1 and 2.)

3. Worst case is determined as a single valve clo-sure with containment pressure on one side ofthe valve and atmospheric pressure further down-stream.

4' Containment back pressure. will have no effect onclosing since the same back pressure will alsobe present at. the inlet side of the cylinder andthe differential pressure will be the same duringnormal operation.

5. Purge valves supplied by Henry Pratt Companydo not normally include accumulators. Accum-ulators, when used, are for opening the valverather than closing.

6..

7;

Torque limiting devices apply only to electricmotor operators which were not furnished onpurge valves for St. Lucie 51 Nuclear Plant.

Review of drawa.ngs 2998-G-862, ( 864) ~ (,865},(-866) ~ (.-867),i (-869), ( 875), ( 878) e .and(-880) shows valves installed j,n straight lengthsof pipe in such a way that flow conditions arestabilized and, thus, does not affect torquecalculations.

8. Calculations were performed, assuming free dis,charge downstream and also assuming outletpiping, the higher torque valises were used.

~ er oe ~ o RPil'5tH~ HQM ~ ~ 0 ~ ~ ~

B. This analysis consists of a static analysis of thevalve components demonstrating. that the stress levelsunder combined seismic and LOCA conditions are lessthan the 90% of the yield strength of the mate "ialsus'ed *

A valve operator structural evaluation is presentedbased on the operator's ability to resist the reactionof LOCA induced fluid dynamic torques.

C. Sealing integrity can be evaluated as follows:

Decontamination chemicals have very littleeffect on EPT and stainless steel seats.Molded EPT seats are generically known tohave a maximum gummulative radiation resis-tance of 1. x 10 rads at a maximum incidencetemperature of 350oF. Xt is recommended thatseats be visually inspected every 18 monthsand be replaced periodically as required.

Valves at outside ambien temperatures below0 P, if not properly adjusted, may have leak-0

age due to thermal contraction of the elastomerhowever during a LOCA, the valve internal temp-erature would be expected to be higher thanambient which tends to increase sealing capa-bility after valve closure. The presence ofdebris or damage to the seats would obviouslyimpair sealing.

~ o e ~ r o io d'L'lea 't0 tl~ I0 0 VI ~ 1 ~ ~ ~

~ 4

~ HETHOD OP ANALYSIS

Valve/Actuator evaluation is. based on fluid dynamic torque

calculation, valve stress analysis and operator evaluation.

A. Torque Calculation

The torque of any open butterfly valve is the sum-

mation of fluid dynamic torque and bearing friction

1

ctorque at any given disc angle.

Bearing friction torque is calculated from the

following equation:

TB — b,p (A) (U) (. Sd)

TVhere,

Pressure differential, psi.2Projected disc area normal to flow', zn

U = Bearing coefficient of friction.Shaft dia., in.

Fluid dynamic torque is calculated from the followingequation:

-

:cI

t

TD=CDhP3

- Nhere,

D = Valve dia. inches.

IP = Pressure differential, psi.

Ct Torque coefficient.

Prat t has developed torque coe fficients for0

different angles of disc opening based on experimen altest data using 5" scale model 'valves with dry airas Fluid medium. Such tests were performed using

"on-center" disc designs at varying upstream/downstream

pressure ratios of 1:1 to 4:1. Similar tests were

performed For "oFE-center" discs at a pressure ratiooF 1:l.

~ ao oo ~ »o ~ till.etl+CJPage 5 of 7

For the purpose of this analysis "off-center" disctorque coefficients have been derived by modification ofexperimentally determined "off-center" disc torque coeffi-cients as described above, incorporating applicable pressureratio factor.

The following output summarizes calculation dataand torque results for valve opening angles of 0 to 90

The maximum valve torque due to flow under specifiedLOCA conditions occurs at the valve angle 75 from the clo ed

position and is equal to 230449 in-lbs. (worst condition).

fj- (: 2 I;> I (j- I

VALVI'. S I r'. I'.:Vbl VF 'I'Y I'I.:S'3RF f Dl A.:~llG. C) L.F. 3F Fl"(:T>I.'I.ATIN (» f'A(:1")h:

INI. I";, f I>foal(SSI JIiE:fIIInRT -S)V I 8 I r<ESS.

')O'I'I I:T I»Ill".SSURE:NAX FL') h ICATI.:I'1IN INUiX S )i~I I ('L')I"VRLVF. INLLT DI.N SI 'I'Y:FULI;)PEN I)El. TA P:SYS'I'!:.'8 C')NDI TI,)NS:

PI PE IN-I'IPE 0UT

7 / ' (5 (1

46 ~ I 18 1 N (;I I K548 IN (:I3-N I< I A

/5 I N CII E 5bi 88(j8AL - 8 3

2548 PS I AP.le(5<518 PSIA" I ULI Y ')f>EN

14 I PSIA47P. /54m CFN p 969327 ~

'2525. 3 Lr»/N I N~ 1 56532 LB/F'ft 3lG ~ 1182 PSI

.) F F S I', T A SYNNi E'f HI C D I 3 C

CI.RSS 15

SCFN > 74881 1

"AND" Al Il SEA VI CE 0 P38 DEG~ F

L O/N IN

ANGL F

85

1815282538354i84i558IS 56()( CS

7 (g

758 (~I

8 598

TH I<') AT( SDELTA P P I<ES S.

~ f'S I HATI ')P.S 38 P. ~ 7P. I28 I I P. 87428 68 2 ~ 878PA. 63 2 ~ 865PB 56 2 8>5828'8 2o 849P8 ~ 3 / 2~ 838PA. PS 2. 82528. 11 2. () I I19 ~ 96 I o 99&i19 ~ 79 I i 97919 ~ 61 I ~ 96219 ~ 4i2 1 ~ 94i419 ~ 22 I ~ 92519 ~ 81 1 o 98618 ~ '/9 I ~ 00 6I(5 ~ 51 ' kg&1I (5 ~:35 1 ~ 84 /18 ~ 12 I ~ 628

)N I C)FL3 (0

( SCFN)8

&11 /15687332/558 18793807

13519218 427723561 5P9 /88335'I (1334i48P. 4i& ~

5/i 5423 .

6599487j3 79 41') 1829'I931 89!i9 637289693P8

FLO 8(L8/N IN )

8467

1191254844427186

10328I 48681798 IP2&j3 8

~ 2725633689416395838 I681537610571 (><5

/35 /314881

TD

5456416374639/8 13

I 54492382239124i61282861 63

IIP335137831I 549 53I 'I 4i28 1

186633P. ()56

SC'38296

285>2 461 72060114987

515419414485393377359337313F67P. 58228197165154I 5'3151149147

. 55879285658548219.

1 5(3 43233993948361 &i2886/i 17

11262213/298I 5518 P.

l 744i78,186799P.858 1P.230 4i492(~)539 I172217115134

. -55{179I-P. I 74PP57 48'.3

15856'-22.644

38 765609 45858 58

I 12845136772154/24174(.'83I C564i&828 55(>323(i I 43P858)51719 18I 14839

'ra aPEV TO CI )SFTB+TH TD+TB+TH TD- TB- TH

SEA'I'ING ~ BEARIi~IG + HUB SEAL T31'OUE (i~1/N) =NAX~ DYN. + LII:.AI;ING + HUI3 SEAL T3 f'CUE (N/, I)

~ ~

55819 INi-l.BS (j 8 DEG.23'49 IN-L)3S 0 75 DEG.

./YO//=,'8//$ 4/I/8Z YS/X /5

B. Valve Stress Anal sis

The calculated maximum valve torque of 230,449 in-lbs.resulting from LOCA conditions is a worst case derivation

of valve torque using'the Paragraph III considerations.

This value is used in the seismic stress analysis, Attach-

ment 3, along with "G" loads per design specification. The

calculated stress values- are compared to code allowables,

C.

if possible, or LOCA allowables of 90% of the yield strength

of the materials used.

0 erator Evaluation

The maximum torque (230,449 in-lbs.) generated during

a LOCA induces reactive forces in the load carrying com-

ponents of the actuator.

The Bettis Model T-520-SR2 furnished has a maximum,

rating of 225, 000 in-lbs. for these components at the fullopen or full closed positions.

The manufacturer has advised that the maximum torque

absorption capability at, any intermediate position between

full open and full closed should be limited to 125,000

in-lbs. per Bettis letter dated May 19, 1980, Attachment 4.

Fluid dynamic torques generated by a LOCA were found

to.be lower than 125,000 in-lbs. only for valve disc openings

of 45 or less.0

Bettis Seismic Analysis Report, R-1062-19 dated December

6, 1976 for Model No. T-520-SR2 is attached as Attachments'

and 6.

........ r%msted~ SOU ~ I el ~ ~

0

V.. Conclusion

It is concluded that neither the valve structure nor

the valve actuator is adequate for the LOCA induced loads

based on calculated torques developed. in this analysis

except for disc opening angles of 45 or less.0

In order to insure the adequacy of the valve struc-

ture it is recommended that the top valve shaft and disc

hub block key be changed such that the minimum insertion

length of key into the hub block is 5.75". This change

would provide for allowable stress levels suitable for

LOCA conditions. In addition, the valve actuator would

have to be changed to a currently qualified model. Note

also that a substantially larger actuator will necessitate

a new check of the operator fit-up to valve trunnion as

well as a re-check of the seismic analysis/operator mounting

section.. A substantially larger actuator may also render

,the valve body structurally inadequate to support the in-creased loading.

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ATTACHMENT 5 3

48"'lA VALVE

STRESS ANALYSIS

STRESS REPORT FOR

48" R1A BUTTERFLY VALVE

PER SECTXON XIIASHE BOlLER AND PRESSURE VESSEL CODE

pro3ect Site St. Lucie Nuclear Power Plant

Customer

Engineer

Unit Nl

Florida Power a Licrht Co.

Ebasco Services, Enc.

Original Specification FSAR Fi ure 6-21A 6 6-21B NY-422237

Orzgzna3. Purchase Order NY-422237

Original Pratt, Job No.

Valve Tag Nos.

7-4491-1

I-FCV-25-1 2 3 4 5 & 6

,General Arrangement Drawing

.Assembly Drawr'ng

E-2184

C-1784

Rev. 5

Rev. 1

Prepared by:

Date:

Reviewed by:

Date:

Certified by:

Date:

i-3 < > ~ lu~ r ~VM

glllltlf)gg

30701REGISTERED

; PRO:ESS(0.'>AhEflGiNEER

~Op ~

'./NO~ „:"00::tlllllllil

Form No. HPCo. 3.172

TABLE OF CONTENTS

Hi RH~ ~WRCg~MCbHPr W~

List of Figures

Nomenclature

Summary Tables

Stress Level Summary

Frequency Analysis Summary

Palve Dimensional Data

Stress Anal sis

Introduction

End Connection Analysis

Body Analysis

Disc Analysis

Shaft Analysis

Disc Hub Analysis

Shaft Bearing Analysis

Thrust Bearing Analysis

Bottom Cover Analysis

Operator Mounting Analysis

Frequency Analvsis

~Pa e

21

27

28

30

31

35

36

42

44'6

50

52

65'

~>

~

LIST OF FIGURES

~Fi . Ne. Title ~Pa e

Valve Body Spatial OrientationBanjo Assembly

Pressure Area Analysis Cross-Section in Body

Disc Hub Block

Thrust Bearing Assembly

Top Trunnion Mounting

Trunnion Bolt Pattern

Bonnet Bolt Pattern

38'0

".Operator Bolt Pattern

Top Trunnion Assembly

1

NOhfENCLATURE

The nomenclature for this analysis is based upon the nomen-I

clature established in Paragraph NB-3S34 of Section III of the

ASME Boiler .and Pressure Vessel Code. Where the nomenclature

comes directly from the code, the reference paragraph or figure

for that symbol is given svith the definition. For symbols not

defined in the code, the definition is that assigned by Henry

Pratt Company for use. in this analysis.

ANALYSIS NOl IENCLATURE

Am

Effective fluid pressure area based on fullycorroded interior contour for calculating crotchprimary membrane stress (NB-3545.1(a)), in

'I

Metal area based on fully corroded interiorcontour effective ig resisting fluid force. on Af(NB-3545.1 (a)), in~

A2

A3

A4

As

A6

A7

A8

A9

Tensile area of thrust bearing adjusting screw.

Tensile area of bottom cover bolt, in

Shear area of bottom cover bolt; in

Tensile area of trunnion bolt, in

Shear area of trunnion bolt, in2Tensile area of operator bolt, in

SLear area of operator bolt, in2

Tensile area of hub retainer bolts

A10 Shear area of hub bolts

All Tensile area of hub bolts

A12 Shear area of thrust bearing retainer bolts

A13 , Tensile area of thrust,'bearing retainer bolts

Bl

B2

B3

B4

B5

B6

B7

Unsupported shaft length, in.

Bearing bore diameter, in.

Bonnet bolt tensile area, in.

Bonnet bolt shear area, in

Bonnet body cross-sectional area, i»

Top bonnet weld si c, i».Bottom bonnet weld size, in.

ANALYSISNOi~fl!NCLATURL'8

B9

Cp

Distance to outer fiber of bonnet from shaft ony axis, 'in.

Distance to outer fiber of bonnet from shaft onx axis, in.A factor depending upon the method of attachmentof head, shell dimensions, and other items aslisted in NC-3225,2, dimensionless (Fig. NC-3225.1thru Fig. NC-3225.3)

Stress index for body bending secondary stress re-sulting from moment in connected pipe(NB-3545.2(b))

Stress index for body primary plus secondary stress,inside surface, resulting From internal pressure(NB-3545.2(a))

C2

C3

C7

Stress index for thermal secondary membrane stressresulting from structural discontinuityStress index for 'maximum secondary membrane plusbending stress resulting from structural discontinuityProduct of Young's modulus and coefficient oflinear thermal expansion, at 500 F, psi/ F(NB-3550)

Distance to outer fiber of disc for bending alongthe shaft, in.

C8

d

Dl

D2

D3

D4

D5

D6

Distance to outer fiber of disc for bending aboutthe shaft, in.Inside diameter of body neck at crotch region(NB-3545.1(a)), in.Valve nominal diameter, in.Shaft diameter, in.Hub retainer bore diameter.

Thrust collar outside diameter, in.Tlirust bearing bolt di amet er, in.Cover cap bolt diameter, in.

ANALYSIS NOMENCLATURE

Dy

D8

D9

10

DllE

Trunnion bolt diameter, in.Operator bolt diameter, in.

Bonnet bolt diameter, in.Diameter of thrust bearing adjusting stud, in.

-Outer diameter of trunnion, in.Modulus of elasticity, psi

F

F

Bending modulus of standard connected pipe,. as givenby Figs. NB-3545.2-4 and NB-3545'.2-5, in.~

1/2 x cross-sectional area of standard connected'ipy, as given by Figs. NB-3545.2;. 2 and NB-3545.2-3,'.i.n.

Natural frequency of respective assembly, hert

Fx

y

Ã3g - -Seismic forcexacceleration actingn

4'3gy- -Seismic forceacceleration acting

along x axis due to seismicon operator extended mass, pounds

along y axis due to seismicon operator extended mass, pounds

Fz

Gb

Gd't

N3gz--Seismic force along z axis due to seismicacceleration acting on operator extended mass, pounds

J Gravitational acceleration constant, inch-per-second 2

Valve body section bending modulus at crotch region(NB-3545.2(b)), in3

Valve bo]y section area at crotch region (Ng-ogag.g(b) ), in

Valve body section torsional modulus at crotch region(NB-3545.2(b)), in~

Seismic acceleration constant along x axis

Seismic acceleration constant along y axis

Seismic accclcration co»'tant along z axis

ANALYSIS NOMENCLATURE

hg

Gasket moment arm, equal to the radial distance fromthe center line of the bolts to the line of the gasketreaction (NC-322S), in.

H3

H4

H~

H6

H7

H8

I2

Disc hub key height, in.

Top trunnion bolt square, in.,Bottom trunnion bolt square, in.Bonnet bolt square, in.Operator bolt square, in.Bonnet bolt. circle, in.Operator bolt circle, in.

Bonnet height, in.Actual body wall thickness, in.

Bonnet body moment of inertia about x axis, in

Bonnet body moment of inertia about y axis, in

'4Disc area moment of inertia for bending about theshaft, in"

Disc area moment of inertia for bending along theshaft, in4

Moment of inertia of valve body, inI

I7

8

Jl

Moment of inertia of shaft, in

Disc area moment of inertia for bending of unsupportedflat plate,in'omentof inertia of top trunnion plate.

Distance to neutral bonding axis for top trunnionbolt pattern along x axis, in.Distance to neutral bcndi»g axis for top tru»»io»bolt pattern alo»g y axis, in.

ANALYSIS NOML'NCLATURE

6

Kl

K~

K~

K6

Distance to neutral bending axis for bonnet boltpattern along x axis, in.

Distance to neutral bending axis for bonnet boltpattern along y axis, in.Distance to neutral bending axis for operator boltpattern along x axis, in.Distance to neutral bending axis for operator boltpattern along y axis, in.Spring Constant

Distance of bonnet leg from shaft centerline, in.Thickness of disc above shaft, in.

. Length along z axis to c.g. of bonnet plus adapterplate assembly, in.

Top trunnion width, in.

Top trunnion depth, in.

Height of top trunnion, in.

Ll

L2

L~

Valve body face-to-face

Thickness of operator ho

Length of engagement oftrunnion, in.

dimens ion, in.using under trunnion bolt, in.

cover cap bolts in bottom

L4 Length of engagement of trunnion bolts in toptrunnion, in.

L~

L6

L7

Bearing length, in.Length of shaft after retainer groove, in.

Length of engagement of bonnet bolts in adapte>plate . in.

L8

L9

Length of engagement ofLength of e»gagcmc»t of

bonnet bolts in bonne t in ~

(Hug )stub shaft in disc,<t».

ANALYSIS NOMENCLATURE

Llo Disc hub key length, in.

Top trunnion weld height

Reciprocal of Poisson's ratioMass of component

My

Hy

M8

lf3(gyZo+gzYo), operator extended mass seismic bendingmoment about. the x axis, acting at the base of theoperator, in-lbs.

N3(gxZ'o+gzXo), ogerator extended mass seismic bendingmoment about .the y axis, acting at the base of theoperator, in-lbs.

Ã3 (gxYo+gyXo), operator extended mass seismic bend'ingmoment about the z axis, in-lbs.Mx+FyTS, operator extended mass seismic bending moment

'about the x axis, acting at the bottom of the adapterplate, in-lbs.My+FxTS, operator extended mass seismic bending momentabout the y axis, acting at the bottom of the adapterplate, in-lbs.Mx+Fy(TS+H8)+gyN4K3, operator extended mass seismicbending moment about the x axis, acting at the baseof the bonnet, in- lbs .

My+Fx(TS+H8)+gx'l<4K3, operator extended mass seismicbending moment about the y axis, acting at the base.of the bonnet, in-lbs.

Bending moment at joint of flat plate to disc hub,in-lbs.

N Permissible number of complete start-up/shut-down,cycles at hr/100 F/hr/hr fluid temperature change

. rate (NB-3545.3)

NA

N2

Not applicable to the anlysis of the system

Number of top disc pins

Number of operator bol.s

Number of trunnion bolts

~,

ANALYSIS NOhtENCLATURH

Pd

Pr

Ps

Pe

Pe6

Ped

Pet

Design pressure, psiPrimary pressure rating, pound

Standard calculation pressureps1

Largest value among Peb, Ped, Pet, psiSecondary stress in crotch region of valve body causedby bending of connection standard pipe, calculatedaccording to NB-3545. 2(b), psiSecondary stress in crotch region of valve body causedby direct or axial load imposed by connected standard.piping, calculated according to NB-3545.2(b), psiSecondary stress in crotch region of valve body causedby twisting of connected standard pipe, calculatedaccording to NB-3545.2(b), psiGeneral primary membrane stress intensity at crotchregion, calculated according to NB-3545.1(a), psi

Pm

Qp

QT

QT2

Primary membrane stress intensity in body wall, psiSum of primary plus secondary stresses at crotchresulting from internal pressure,- (NB-3545.2(a)),ps1

Thermal stress in crotch region resulting from 100 F/hr fluid temperature change rate, psiMaximum thermal stress component caused by throughwall temperature gradient associated with 100 F/hrfluid temperature change rate (NB-3545 '(c)), psiMaximum thermal secondary membrane stress resultingfrom 100 F/hr fluid temperature change rate, psi

Ql

e,

Maximum 'thermal secondary membrane plus bonding stressresulting from structural discontinuity a»d 100 F/hrfluid,teaiperature change rate, psiDistance to bolts in bolt pattern on hub block, in.Distance to bolts in bolt pattern on hub block, in.

ANALYSIS NOMENCLATURE

Q3

Q4

Q5

Qs

Q7

Distance to bolts in bolt pattern on hub block, in.Distance to bolts in bolt pattern on hub block, in.Distance to bolts in bolt pattern on hub block, in.Distance to bolts in bolt pattern on hub block, in.Distance from shaft centerline to disc plate, in.Mean radius of body wall at crotch region

(Fight

NB-3545.2(c)-1), in.

'2

R4

R5

Rm

R6

Sm,

Sn

Spl

Sp2

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.Disc radius,, in.Shaft radius, in.Mean radius of body wall, in.'Radius to gasket in cover cap, in.Distance from shaft centerline to retaining bolt ofthrust bearing.

Assumed maximum stress in connected pipe for cal-culating Pe (NB-3545.2(b)), 30,000 psiDesign stress intensity, (NB-3533), psiSum of primary plus secondary stress intensitiesat crotch region resulting from 100 F/hr temperaturechange rate (NB-3545.3),psi

Fatigue stress intensity at inside surface in crotchregion resulting from 100oF/hr fluid temperaturechange rate (NB-3545.3), psiFatigue stress intensity at outside surface incrotch region resulting from 100oF/hr fluid temp-erature chango rate (NB-3545.3), psi

S(1) through S(83) are listed after the alphabetical section ~

10

ANALYSIS NOMENCLATURE

tm

Te

hT2

Minimum body wall thickness adjacent to crotch forcalculating thermal stresses (Fig. NB-4545.2(c))-1),in.Minimum body wall thickness as determined byC.C. 1678, in.Maximum effective metal thickness in crotch regionfor calculating thermal stresses, (Fig. NB3545.2(c)-1), in.Maximum magnitude of the difference in average wal'1temperatures for walls of thicknesses te, Tresulting from 3.00 F/hr fluid temperature changerate, oF.

T2

T3

T4

T5

T7'8

T9

T3.0

T12

UZ

U3

"

U4

Thickness of cover cap behind bolt head; in.Thickness of adjusting screw head, in.Thrust collar retaining plate thickness, in.Cover cap thickness, in.Adapter plate thickness, in.Thickness of bottom 'oonnet plate, in.Thickness of top bonnet plate, in.Maximum required operating torque for valve, in-lbs.Shaft retainer thickness on hub

Bottom cover plate "thickness

Top trunnion wall thickness

Thickness of top trunnion platoArea of bottom bonnet weld, inArea of top bonnet weld, in

Thrust bearing coefficient of frictionBearing friction torque due to pressure loading(shaft journal bearing)

ANALYSIS NOMENCLATURE

V3

V4

vs

v,V7

V8'earing

friction torque due to pressure loading plusseismic loading (shaft journal bearings)

Thrust bearing friction torque

Distances to bolts in bolt pattern on adapter plate, in.Distances to bolts in bolt pattern on adapter plate, in.

Distances to bolt's in bolt pattern on adapter plate, in.

Distances to bolts in bolt pattern on adapter plate, in.

Distance to bolts in bolt pattern on bonnet, in.Distance to bolts in bolt pattern on bonnet,'n.Distance to bolts in bolt, pattern on bonnet, in.

Distance to bolts in bolt pattern on bonnet, in.W Total bolt. load, pounds

W -.1.W

W~

W4

W,

W7

W

X

Y'

Zo

Valve weight, pounds

Banjo weight, pounds

Operator weight, pounds

Bonnet and adapter plate assembly weight, pounds.

Weld size of'isc structural welds, inches

Weight of disc, pounds

Length of weld around perimeter of bonnet, in.

Eccentricity of center of gravity of operator extendedmass along x axis, inches

Eccentricity of center of gravity of operator extendedmass along y axis, inches

Eccentricity of center of gravity of operator oxtondcclmass along z axis, inches

ANALYSES NOMENCLATVRE

Zl

Z2

Z3

Bending section modulus of bonnet, welds in xdirection, in3

Bending section modulus of bonnet welds in ydirection, in3

Torsional section modulus of bottom bonnet welds,3.n 3

Torsional section modulus of top bonnet welds,1n3

dy

Z7

Z8

Maximum static deflection of component, inches

Distance to edge of dis'c hub, inches

Thrust bearing stud diameter, in.

13

ANALYSIS NOhIENCLATURE

S (1)

S(2)

S(3)

S(4)

S(S)

S (6)

Combined bending stress in disc, ysiBending stress in disc due to bending along theshaft, psiBending stress in disc due to bending about theshaft, psi

Combined stress in shaft, psiCombined bending stress in shaft, psi

Combined shear stress in shaft, psi

S (7)

S(8)

S (9)

S (10)

Bend'ing stress in shaft due to seismic and. pressureloads along x axis, psi

Bending stress in shaft due to .seismic load alongy axis, psiTorsional shear stress in top shaft due to operatingtorque, psiDirect shear stress in shaft due to seismic andpressure loads, psi

S(ll) Shear tear out of retainer in shaft groove,, psi

S(12)

S (13)

S (14)

S (15)

S (16)

S(17)

S (18)

S (19)

S (20)

S (21)

S(22)

.Shear tear out of shaft groove, psi.Bearing stress on retainer and groove, psi.Tensile stress in retainer bolts, psi.Bearing stress on hub key way, psiShear stress on key, psi.Combined= stress on hub block bolts, psi

Combinod tensile stress on hub block bolts, psi.Shear stress in hub block bolts, psi

Shear tear out of shaft thru hub block, psi

Comprcssivo l,oad on shaft bearings, lbs,

Bearing stress on thrust collar, psi.

ANALYSIS NOMENCLATURE

S(23) Shear stress in adju'sting screw head, psiS(24) Combined stress in adjusting screw, psiS(25) Direct tensile stress on adjusting screw, psiS(26) Torsional shear stress on adjusting screw, psiS (27) Shear stress in adj usting screw threads, psiS(28) Combined stress in retainer bolts, psi.S(29) Tensile stress in retainer bolts, psiS(30) Shear stress in retainer bolts, psiS(31) Shear tear out of thrust bearing bolts, psiS(32) Shear stress in cover plate, psiS (33)

S (34)

S (35)

S (36)

Shear tear out of cover cap bolt head through bottomcover cap, psiCombined. stress in cover cap bolts, psiShear stress in cover cap bolts due to torsional

~ loads, psiS(37) Direct tensile stress in cover cap bolts, psiS(38) Combined stress in cover cap, psiS(39) Radial stress in cover cap, psiS(40) Tangential stress in cover cap,. psiS (41)

S(42)

S (43)

S (44)

Shear stress in cover cap, psiShear tear out of trunnion boltin trunnion, psiHearing stress of trunnion bolttlunnion, psiHearing stress of trun»ion boltbonnet plato, psi

through tappod hole

on tapped hole in

on through hole i»

S(45) Shear tear out of trunnio» bolt head through bo»notplato, ps1

ANALYSIS NOMENCLATURF.

S(46) Combined stress in trunnion bolt, psiS('47) Direct tensile stress in trunnion bolt, psi

S(48) Tensile stress in trunnion bolt due to bendingmoment, psi

S(49$ Direct shear stress in trunnion bolt, psi

S(50) Shear stress in trunnion bolt due to torsional load,psi

S(51) Shear tear out of bonnet bolt through tapped holein adapter plate, psi

S (52)

S (53)

S (54)

Bearing stress of bonnet bolt on tapped hole inadapter plate, psi

Bearing stress of bonnet bolt on through hole inbonnet, psiShear tear out of bonnet bolt head through bonnet,ps 3.

S (55) Combined . stress in bonnet. bolts, ps iS(56) Direct tensile stress in bonnet bolts, psiS('57) Tensile stress in bonnet bolts due to bending moment,

psi ~

S(58) ~ Direct shear stress in bonnet bolts,psi.'(59)

Shear stress in bonnet bolts due to torsionalloads, psi

S (60)

S (61)

S (62)

S (63)

Shear tear out of operator bolt head through adapterplate, psiBearing stress of operator bolt on through hole inadapter plate.Combined stress in operator bolts, psiDirect tcnsilc stress in operator bolts, psi

S (64) Tcnsilc stress in operator boltps'uc to bending moment,

S(65) Direct shear stress in operator bolts, psi

ANALYSIS NOMENCLATURE

S(66) Shear stress in operator bolt due to bending moment,PS1

S(67) Combined stress in bonnet body, psi

S(68) Direct tensile stress in bonnet body, psi

S(69) Tensile stress in bonnet body due to bending moment,PS1

S(70) Direct shear stress in bonnet body, psi

S(71) Shear stress in bonnet body due to torsional load,PS1

S(72) Combined shear stress in bottom bonnet weld, psi

S(73) Total tensile stress in bottom bonnet weld, psi

S(74) - Direct tensile stress in bottom bonnet weld, psi

S(75) Tensile stress in bottom bonnet weld due to bendingmoment, psi

S(76) Total shear stress in bottom bonnet iield, psi

S(77) Direct shear stress in bottom bonnet weld, psi

S(78) Shear stress in bottom bonnet weld due to torsionalload~ ps1

S(79) 'ombined shear stress in top bonnet weld, psi

S(80) Total tensile stress in top bonnet weld, psiS(81) Direct tensile stress in top bonnet weld, psi

S(82) Tensile stress in top bonnet weld due to bendingmoment, psi

S(83) Total shear stress in top bonnet weld, psi

S(84) Direct shear stress in top bonnet weld, psi

S(85) Shear stress in top bonnet weld duo to torsionall load, psi

S(86) Combined stress in top trunnion welds, psi

ANALYSIS NOW I!NC LATU RE

S(87) Shear stress in trunnion welds, psiS(88) Torsional shear in trunnion welds, psiS(89) Combined stress in top trunnion body, psi.,

S(90) Direct tensile stress in top trunnion body, psiS(91) Bending tensile stress in top trunnion body, psiS(92) Direct shear stress in top trunnion body, psiS(93) Torsional shear stress in top trunnion body, psiS(94) Combined shear stress in top trunnion to shell weld, psiS(95) Shear stress due to operator eccentricityS.(96) Torsional stress due to operator eccentricity and

operating loads..

SUi~li~lARY TAISLI! INTROI)lKTION

In the following pages, the pertinent data for the buttcr-fly valve stress analysis is tabulated in throe categories:

1 Stress Levels for Valve Components

2. Natural Frequencies of Components

3. Valve Dime»sional Data

In Table 1, Stress Levels for Valve Components, the followingdata is tabulated:

Component Name

Code Reference (when applicable)Stress Level Name and Symbol

Analysis Reference Page

Material SpecificationActual Stress Level

Allowable Stress Level

The material specifications are taken from Section II of the

code when applicable. Allowable stress levels are Sm fortensilo stre'sscs and .6 Sm for shear stresses. The allowablelevels 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 Frequoncios of Valve Components, tho

Summar Table Introduction

Component Name

Natural Frequency Symbol

Analysis Reference Pago

Component Material

Natural Frequency

In Table 3, Valve Dimensional Data, the values for thc

pertinent valve dimensions and parameters are given.

TABLE STRESS LEVELS FOx E COMPONENTS

COMPONENTCODE REF.PARAGRAPH SYMBOL & NAME

REF.PAGE MATERIAL

STRESSLEVEL, PSI

ALLOWABLESTRESS LEVEL

PSI

BODY NB-3541.1

NB-3545. 2

Primary membranestress in crotchregion

Primary membrane

Pr'imary plus secon-dary stress due tointernal .pressure

Ip

m

37

37

39

ASTM A-516 GR.60

ASTM A-516 GR.60

ASTM A-516 GR.60

1941

1264

1174

Sm15000

Sm15000

Sm15000

NB-3545.2 Pipe reaction stressAxial load P d

Bending .load P eb

39ASTM A-516 GR.60

- 3288

5981

1.5Sm22500

Torsional load 'et 5981

NB-3545.2

NB-3 545. 2

Thermal SecondaryStress

Primary plus secon- Sdary stress n

39

39

ASTM A-516 GR.60

ASTM A-516 GR.60

678

7370

Sm15000

3Sm45000

NB-3545.3 Normal duty fatiguestress Na ~ 2000

S n 40 ASTM A-516 GR.60 6713 Sm65000

DISC NB-3546.2 Combined bendingstress in disc

S (1) 41 ASTM A-516 GR.60 9062 l. 5Sm22500

SHAFT NB-3546. 3 Combined stress inshaft

S(4) 42 ASTM A-479 Type 304 21350 .9Sy =27000

E'

TABL STP-=S LEVELS FO~ VE COi PONENTS

CODE REF.COl~PONENT PARAGRAPH SY|~IBOL & NAYiE

REF.PAGE Ã&TERIAL

STRESSLEVEL, PSX

ALLONABLESTRFSS LEUFL

PSZ

$ 5 w~

RE A|NERShear ear out ofretainer in shaftgroove

S (11) 43 ASTH A 240 Type 304 2198 . 6Sm9180

Shear tear out ofshaft groove

Bearing stress onretainer & groove

Tensile stress inretainer bolts

S (12)

S (13)

S (14)

43 AST?I A240 Type 304

43 ASIDE SA 540 CL. 1GR. B-21

43 AST&I-A-479 Type 304 1229

2320

19285

.6Sm9960

Sm15300

Sm33000

.":UB BLOCKS Bearing stress onhub key way .

Shear stress on key

Combined stress onhub block bolts

S (15)

S (16)

S (17a)

44

44

44

ASTH A 350 GR.LF1

AXSI C4140

ASi~IE SA 540 CL.1GR. B-21

32683

16342

80109

.9Sy27000

. 6Smla800

.6 yield= 90,000

Shear tmrout tapedholes in disc

S (17b) 44 AST?I A-516 GR.60 16025 .54Sy =17280

SHAFTB AR|:NGS

:HRt:ST:-=AR ZG

Shear tearout ofshaft thru hub block

Compressive load onshaft bearings

Bearing stress onthrust collar

Shear stress in ac',—

ust ng screv head

S(20)

S (21)

S (22)

S(23)

44

46

47

47

AST?I A-516 GR.60

Roller Bearing

AS' 4.38 GR.lType iX

AS?IE 479 Type 304

6250

686384,

1403

4176

.6Sm9000

Sm3000

0.6Sm9960

s

~ ~

~ s ~ ~ r s ~ s ~ ~

~ ~ s

~ ~

~ ~ ~ ~ I~ ~

~ s ~ ~ - I ~

~ ~ ~

I s r r I

~ ~ ~

s I s

~ ~ ~ ~

~ ~ ~

~ ~ ~

~ ~ ~ ~ ~

~ ~ s s~ ~

~ ~ ~

~ ~ ~ ~ ~ ~ ~

Is I~ I

~ ~

s s ~ ~

~ ~ ~ ~ ~

~ ~

s r I

~ ~

~ ~

TABLE STRESS LEVELS F LVE COMPONENTS

COMPONENT

OperatorIloun tingContinued

CODE REF.PARAGRAPH SYMBOL & NAME

Shear tearout, ofbonnet bolt headthrough bonnet..

Combined stress inbonnet bolt

REF.PAGE

S(54) 56

S(55) 56

MATERIALSTRESS

LEVEL, PSI

N/A

N/A

ALLOWABLESTRESS LEVEL

PSI

Shear tearout ofoperator bolt headthru adapter plate

Bearing stress ofoperator bolt onadapter plate

S (60) 58'SME SA-36

S(61) 58 ASME SA-36

2560

7670

.6Sm'560

Sm12600

Combined stress inoperator bolt

S (62) 58 ASTM A-540 CL.lGR. B-21

19580 Sm33000

Combined stress in S(67) 60bonnet body

Combined shear stres S (72) 60in bottom bonnet wel

N/A

N/A

TOPTRUNNION

Combined shearstress in top trun-nion plate welds

Combined stress intrunnion body

Combined shearstress in top

trun-.'ionto shell weld

S(86) 62 ASTM A-516 GR.60

S(89) 62 ASTM A-516 GR.60

S (94) 64 ASTM A-516

3042

7860

2820

Sm15000

Sm15000

.6Sm9000

Table 2 NATURAL FREQUENCIES OF VALVE COMPONENTS

ComponentName

NaturalFrequency

Symbol-Re|.Page Material

NaturalFrequency

(Hertz)

BODY 65 ASTM A-.516 GR,60 822,7

BANJON2

66'STM A-516 GR.60 110.5

COVER CAPN3 66 ASTM A-516 GR.60 1590

VALVE ASS'Y FN0 67 109.2

- DIMENS'IONAL DATA

Job Number: D-027270-1 Valve Size: 48" NRlA

Operator Mounting:Ada ter Direct OperatOr: T-520 SR ettis

282.684A~

A 11.14113

Al /Az

'3

.1419

A4 .1257

A5 .969

.302

(3. 032)or

A6

A7 .334

A8

Ag 0. 1063

A '' 0 ~ 551

0.606

A 0- 125'7

A13 0.1419

Bl asc n yBz 6.752

N/A

N/A

B N/A

B N/A

N/A

N/A

N/A

0.3

3.892iud HQg~p

Cb

C

Cz

C3

C,.

3.

0.45

0.55

238.80

D6

0.5 (8)

0.5 (3)

1.25D7

DS 0 75

DgN/A'10

1.25

D 10 '

E 29 x 10 6

F 650

F 29

F See Table 3n

FX

3495

C7 2.0

C8 2.0

d 6.752

d 49.o87

Dl . 48 disc dia.)

Dz 4.7S

D3 4.25

D4 3.0

F)'-~

Fz

3495

4660

(32. 2) 386

Gb 3260.54

G 264.6

G 6521't

gx 3

fy

h.gHl

Hz

1. 25

12.188

I6

24.988

H3 N/A(4.25 rad.)

H4 N/A(12.188)

N/A

H /A

H7 . 14-0

N/A

Hg 1 6565

I N/A

I N/A

249.16

269.16

112336

Jl < 1.281

J2 1.281

l. 281

J4 1 271.

J5 7.o

7.O

N/A

K2 1.50

K3 O.719

K4 14,75

14. 75

K6 7.125

Ll 20'. 0

L3 . 625

L4 1.375

(4.s)

o.s

L7 1 38

Lg 10.7

Llo 4.7S

M

M

MZ

M"X

Na

N

N

N3

P~

P

Ps

Pe

Pb

Pea

P

P

P 'm

QT

QTl

Dimensional Data (Cont.)

I7 198.4

rs

. 625+ (1f2}

3'. 4

55523'.9''75'3

6.'3'5365.1

60547.96

42560.36

60720.52

42732.92

2000

75 (42)

75

5981

5981

3288

5981

1941

1.264

1174

677.46

570

Q 107.46Tz

131.34T3

Q 1.5. 1Q

~ 6.S2

Q 8.S3

Q 2.4384

2.2825

Q 9.9366

Q 3.12S7

4 ..188

1 24.59353.

T'~ 5

R4 23.359

R 2.37s

R 4.875

R 4.25

27.07825

$ 30000

$m

$ 7369.5n

1950 31Pl

267 12 ~ 88pz1.656S

e

t .59m

T 2.25e

~T2

T1

T2

T3

T4

T5

.T6

T7

. T

. T9

. T10

T11

T1

U2

U3

U

U

U6

. V

V2

'

3'

V'

V5

6

V7

1.0

1.38

.5

.25

1.38

1.438

N/A

N/A

230,449

0.25

1.38

1.624

,1..125,,

N/A..

.25

515.

600

2180

0.908

4.696

10..054

13.842

N/A

N/A

N/A

~ Dimensional Data (Cont.)

( V8 N/A

Wl 5900

WZ 2050

Wg 1165

W4 80

W6 N/A

.W7 1950

W< N/A

Xp 4.56

O'42

Zp 4.66

Zl N/A

Z2 N/A

Zg N/A

Z4 N/A

Z7 0.8595

Z8 1.25

ANALYSIS INTRODUCTION

Described in the following pages is the analysis used inverifying the structural adequacy of the main elements of the

air purge butterfly valve. The analysis is structured to comply

with Paragraph NB-3550 of Section III of the ASME Boilder and/

Pressure Vessel Code (hereafter referred to as the code) . Inthe analysis, the design rules for Class 1 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 designrules for Class 2 and 3 are exceeded by the- rules for Class 1

valves..

The air purge valve is designed in accordance with Code

Case 1678 of the code.

Valve components are analyzed under the assumption that thevalve is either at maximum fluid dynamic torque or seating against,the maximum design pressure. Analysis temperature is 300 F.

Seismic accelerations are simultaneously applied in each of threemutually perpendicular directions.

Seismic loads are made an integral part of the analysis by .

the inclusion of the acceleration constants gx, gy gz The

symbols gx, gy, gz represent accelerations in the x, y and z

directions rcspectivel'y. These directions are defi»ed with rc-spect to thc valve body ccntercd coordinate system as illustratedin Figure l. Specifically, the x axis is along the pipe axis,the z axis in along the shaft axis, and the y axis is mutuallyperpendicular to thc x and z axes, forming a right ha»d triadwith them.'

Anal sis Introduction~ ~

Valve orientation with respect to gravity is taken into

account by adding the appropriate quantity'o the seismic

loads. The justification for doing this is that a gravi-

tational load is completely equivalent to a lg seismic load.

The analysis of 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. Where 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 components. Detailed sketches are provided

throughout the report to clearly define the geometry.

Vfil.VE llOAY <:I:l.'I I'.I'CO

COOi<D I IIRI I SY'GATI."tl

I 1

/

F l GURE 2 - ESS Et'T I AL FEATUI'ESOF BANJO ASSEHBLY

SHAFT RETAINER SLIPS INTOGROOVE A!iD I S BOLTED TO)IUB BLOCK.

TOP STUB SHAFT

OPERATOR KEYiNY

DETA.IL OF SHAFTGROOVE 0

Q

HUB BLOCK KEY( AY ISOi'( BORE OF TOP HUBBLOCK Ot<LY

HUB

BLOCKSSHAFT RETAIHERBOLTS

SHAFTRETA I IIERS

DISC

80TTOtl STUB SIIAf'T

FLANGE ANALYSIS

The flange analysis is in accordance with Appendix II,Para. VA-5G of Section VIII, Division I, of the ASllE Codesfor Pressure Vessels and AHWA C-207.

BODY ANAJ.YSIS

The body analysis consists of calculations as detailed inParagraph NB-354.0 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.. Nhere inter-pretation unique to;the calculation is necessary, it is explained

in the sub-section 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 require-ments for standard pressure rated valves.The actual minimum wall thickness in the purge valveoccurs behind the seat retaining screws.

2. Body Sha e Rules

The air purge valve meets tho rcquiremcnts of Paragraph

NB-3544 of the code for body shape rules. The external

fillet at trunnion to body intersection must be greater thanthirty percent of the minimum body wall thickness.

3. ~Primer Membrane Stress Duc tc Entcrnal Prcssure

'Paragraph NB-3545.1 defines the maximum allo»able

stress in t'e neck to flow passage junction. In a but-

tcrfly valve, this corresponds wI.th the trunnion to

body shell junction. Figure 3 shows the geometry through

this section.

The code defines the stresses in the crotch area

using the pressure area method. The equation presented

is found in paragraph NB-3545.1.\

Pm (Af/Am + . 5) Ps.

Applying the code rules to the crotch region re-

sults in a membrane stress considerable less than ifapplied to the region not containing the trunnion. The

trunnion increases the metal area (Am) which decreases t1.e

Af/Am ratio and reduces the result. For a section not con-

staining the trunnion, the fluid area to metal area ratio(Af/Am) reduces to the body inside radius to the shell

'hickness (11m/IIq) since the depths arc the same. The re-suiting membrane stress equation is then:

Pm = (Rm/IIg + .5) Ps

This equation results in the highest stressed/

area and complies with the intent of the code.~ ~

A. Body Primary plus secondary stress due to internal'1

pr cssurc

P RESS URI".-AREA ANALYSIS

BODY CROSS-SECTlOiN

Figure 3

Par"r gr apll NB-354 5. 2 (a) of Scc t ion I I I o E tire code

defirrcs thc formulas used in calculatirrg tlris stress.

Qp = Cp ri + .5

B. Secondar> stress due to pipe reactiorr--Para, NB-3545.2(b)

gives the formulas for finding stress duc to pipe reaction:

Ped = I-'dSDirect or axial load effect

C'q

eb b"'b = Bendieg 1oed effectGb

et " = Torsional load effect

C. Thermal secondary stress--Para. NB-3535.2(c) of Section

I I I of tire code gives Eormulas Eor dctcrmini»g thc thermal

secondary stresses in t)re pipe.

QT QT1 + QTZ

where

QT2 = C6C2LT2

D. Primary plus secondary stresses--This calculatiorr is per

Para. NB-3545.2 and is the sure of the tlrree previous

secondary stresses:

i

Sn =Qp + Pe + 2Qt2 3Sm

5. Valve Eati.r,ue grec ui rcmcnts--Para. NB-3545.3 cl'ccti.on III of

the code defirrcs requirements for, normal dut'alvc fa ti gue.

The allowable stress level is found Crom l:i gute .1-9. rr. Since

the number of cycles is unknown, a maximum va.luc of 2000 is

assumed. The allowable stress can then be fourrd from Figurc

I-9.1 for carbon steel. This then gives a» rllow<rbls stress

I'

of 6S000 psi.S ~= 2/3Q + P b/2+QT3+ 1 ~ 3QTjp1 p e

S 2= .aQ + P,b. + 2QT3

p'

where:QT3 = C6C3672

DXSC ANALYSXS

Section NB-3546.2 defines the design requirements of the

valve disc. Both primary bending and primary membrane stress

are mentioned in this section. For a flat plate such as the

butterfly 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 than one-half

the thickness, membrane stresses are not applicable to the

analysis.

Figure 5 shows the disc for the air purge butterfly valve.

The disc is designed to provide a structurally sound pressure

retaining component while providing the least interference to

the flow.

Primar Bendin Stress

Due to the manner 'in which the disc is supported, the

disc experiences bending both along the shaft axis and about

the shaft axis.. The combined bending stress is maximized at

the disc center where the maximum moment occurs. The moment

is a result of a uniform pressure load.

Combined bending stress in disc:32

S'(1) = S(2) + S(3) + + M2

Where,'

(2)(. 90413 P R4 + . 5B1P mR4 ) C7

3 2

-~ 6666 P R4 CB

— Bending stress due tomoment along shaft axis,psi

S(3) =Z3

P .7854 RA„

t

= Bending stress due to moment.about shaft axis, psi

-'i1

SIIAFT hihl,YSIS

The shaft is analyzed in accordance with Para NB-3546. 3 of.

Sectio'n EEI of the Code. The shaft loading. is a combination of

~seismic, pressure,. and opexating loads. i~laximum torsional loading

is either a combination of. seating and bearing torque or bearing

and dynamic torque. Columnar stress is not considered in the

shaft, loading due to its'egligible effect on the stress levels.

Figure 2 shows the banjo assembly with the stuo shafts,

Shaft stresses due to pressure, seismic, and operat'ng loads:

S(4)=S(S) + (S(5)2+4 S(6) 2)

2 2

lfhe re:l

S(5)=(S(.7) +S( 8) )" = Combined bending stress, psi

R42Ps+Y~gx) < 5 lail(a. 25R54

S( '8 ) = ~.~SI'EZg 8] g~

,25 ~ RS"

S(6)=(S( 9) +S(10) ) ~

S( 9)=.MRS

. 5<RS 4

I<'endi»g, tensile st> cssclue to l)ressurc and seismicloads along x axis, psi

i<ending tensile stressdue to seismic loads along

axis ~ pslCombined shear stress, psi

Torsional shear stress, psi

S(10 )=1.333 . S~R42p +. Si'f>(g.2+g,2) ~

MRS

l)iroct shearstress psi

g 6A.~C~ TOP-~~'E.

'SIIAI'T RLTAINI!R'SSI!HBI,Y

The shaft retainer assembly consists of the shaft re-

tainer, the shaft retainer bolts, and the grooved end of the'I

.stub shaft as shown in figure 2. The shaft retainer, bolts,and shaft groove are loaded by the seismic force of the disc.

1. Shear tear out of retainer in shaft groove.

S(11) = Ng g~@DE 1D

2. Shear tear out of shaft groove.

S(12) = Ã2

mD3

3. Bearing stress on retainer and groove.

S{13) = 4 ti'2 gz~rr DP DS2)

4. Tensile. stress in retainer bolts.

S(14) = 'lUg gz4 Ag

HUB BLOCK ASSEMBLY

The hub block assembly consists of the hub block, the

hub block retaining bolts, and the hub block keyway.

1. Bearing stress on hub keyway.

2 T8R H L

5 1 10

2. Shea'r stress on key.

S(16) = 8

R5H1L10

3. Combined stress on hub block bolts.

( 2' (1'8) + (S(18) + '4 S(19) )

2, 2.Q

2 2

.Where,

S (18) A'1

ll2

mD1. s ' x 1 „(Bl,+Q4+Q

1 2 3

W29 (QT+T/2) 'l~('. Q, + Q,

Q5 + (Q5 + 06)

= Combined tensile stress in bolts due totorsional, pressure and seismic loads.

S(19 = 2g = Shear stress in bolts dne to10 seismic load.

4. Shear tear out of shaft thru hub block.

mP R4 + W2g2

s 4 2 x2 L (K + .5D )

9 2 2

NOTE: T/2 = 1/2 disc thickness.9ESTIIJ<, ToRQUE =CSS 07Q 'O~+ )

(

FlGURC 9

HUG BLOC}w

DtHCMSIOHS

Q6

I

I

Qz I

I

I

I 7

I

I

Q4

I

I

Y

SHAFT HEARING ANALYSES

The sleeve bearings in the trunnion are subjected

to both. seismic,and pressure loads.

S (21);— ~ Pg R4 +N2 (g +g 2) <21 2

X

2

Compressive load onshaft bearing, lbs.

TFIRUST HEARING ANALYSIS

As seen in Figure 5, the thrust bearing assembly is

located in the bottom trunnion. It provides restraint forthe banjo in the z direction, assuring that the disc edge

remains correctly positioned to maintain optium sealing. For-

mulas used to analyze the assembly are given below.

1.'earing stress on thrust collar due to seismic load.

S(22) =

78 5 (D4 D10

2. Shear stress in adjusting screw head due to seismic load.

S(23) = ~~2gz"D10T2

3. Combined stress in adjusting screw.

S(24) = .S(25) + (S(25) 2 ~ 4S(26) 2)

Where:

S(25) = >~Zg, Direct tensile stress due to .

seismic load.

S (26) = 16U6 = Torsional shear stress due to thrustbearing seismic friction torque.

U6. = 1(2gz '3 ( ~ SD10 + ~ 5 (D4 "D10 )

4. Shear stress in adjusting screw threads due to seismic

loads.

S(27) = W2g,<D10T10

S. Combined stress in retainer bolts due to seismic loads.

S (28) = S (29) + (S (29) 2 +4S (30) 2) -'

F IGUftE 5

ESS Em' AL FCmun ES OFTIIRUST DERf< I tiG ASSEIIDLY

VALVE SOnV

SHAFT

TIIPUST MRSHEP

r

1

~7

~~IllIiETR I'tl I WG S CPEll

BOTTOAl COVER

COVLl' Af'

Thrust Bearing Analysis

Where:

s(2o) =. >~>q,

~~aS(30) = U6

a R7 A12,

Tensile stress due to seismicload.

Shear stress due to seismicload.

6. Shear tear out oE thrust bearing retainer bolts.s(31) = w2g

~ Q~ Q~a~

BOTTOM COVER ANALYSIS

Figure 5 shows the bottom trunnion assembly,

including the bottom cover and bottom cover bolts.1. Bottom Cover Bolt Stresses

The bottom cover experiences loading from

the weight of the banjo and from pressure

loads. In determining stress levels, the

bolts are assumed to share torsional and

tensile loading equally..Shear tear out

~ trunnion:

of bolts through tapped holes in

S(33) = N2g< + ~ sR6

L3

Shear tear out of bolt heads through bottom cover,

ps%:

S(34) = W,gz 'P,R6>VI~1~ D6

Combined stress in bolts,psi:'(3S)

= S(37) + (S(37) + 4S(36) )2

Where:

S (36) = 1J

A4Shear stress inbo1 t s due totorsional load

50

Bottom Cover Anal sis2

S(37) = N2gz + mP R6~A~ = Tensile stress inbolts due to seismicand pressure loads,psl

2. Bottom Cover Stresses

The combined stress in the bottom cover is

calculated using the following formulas:

S'('3'8l = S'(39) + S(40) q ((S(39) ~ S (40)) +4 S(41) ) '2

lUher e:

S(39) =. 3(.785(D +.25) 2P ~iU~ z)T42

S(40) 3(,.785(D4+.25) 2Ps+IU2gz)

4 mT4 m

S(41) = .785(D +.25) P +lUq z

~ (D4+. 25) T4

Radial Stress

TangentialStress

Shear Stress

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 6

1. Bolt stresses and localized stress due to bolt loads.

The following assumptions are used in the development

of the equations:

Torsional, direct shear, and direct tensile loads are

shared equally by all bolts in the pattern.B. 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 o fin top trunnion.

S(42) = Fz+W4gz +

trunnion bolt through tapped hole

bT~ (J2+Hp) H (J+H)2) 2)J) li ) Ji )J )

'. 9v L4D7

b. Bearing stress on tapped h'oles in trunnion.

S(43)

c. BearingS(44)

i,,), i'I:„) ))) «i)) )*)')'70»

)

D7L4

stress on through hole in bonnet.

)M,' *Ã,'" ) '" )i,') )"4).»i

D7Tg

Qpcl ator l~founting Analyszs

d. Shear tear out of trunnion bolt heads through

bonnet.

S(45) Fz+{If4gz + i~i> (J2+f{2) + lf (Jl+f{2)2J2'+ 2 (J2+ 1'{2) 2, 2 J12+ 2 ( J 1~ {{2) 2

5. 2 D776

c. Combined stress in trunnion bolts (Sce Fig. 8)

S(46), S(47)+S(48) + ((S(47)+S(48))2+4 (S(49)f+ S(50) ) 2) -'.

2 2

4'here

0

S(47)

S(48)

Fz+li'4gz = Direct Tensile Stress4 A5

{ ~( 2+{{2) f ( 1+.<2)

2J2 +2 (J2+l{2) ZJ1 +2(J1+f{Z)

A5

(4 ) = (F> -''+'~ (g +g )'A6

S(50) = (W,+ r8)(.707 Hp) 4 A6

psi

Tensile stressdue to extendedmass bendingmoment, psi

Direct'hearstress, psiShear stress due totorsional load, psi

Shear tear out of bonnet. bolt through tapped hole in

adapter plate.S(51) = " + "~x(J4+H1) ~(J" +{14)

. ~

4 2J4 +2(J4+i{4) 2 2Jq +2(J-+~!'1)".9lt D9 1

g. Bearing "tress on tapped holes in adapter plate.

S(52) - bfz+78 + (F~ +F 2)

(.707 l{{)4 4

D9{.P

H2

H 2

TOP TRUNNION BOLTING

Figure 7

0 cl ator ilount'1np, Anal 'sl 5

h. Scaring stress on throu ~f> hoj.cs in bonnet.

S(53) = hl z+|'g (Fq> I q 2)<(.707 H,))4

Dg T7'.

i. Shear tear out of bonnet bolt head tfirough bonnet

S(54) =. f z ~ i~I~(J4+ll4) + ii),(Jy+ff4)4 2J42+>(J4+ll4) 2 ZJ~ 2(J +H~) 2

5.2 D9T

j. Combined stress in bonnet bolts (Sce Fig. 9)

S(SS) = S(56)+S(57) . ((S(56) S(57))2',(S83).S$ 9 ))2)-'2 2

I

Nhere

.,S(56) = f:2,

4 Bg

= Direct Tensile Stress, psi

S ( 57) i~f)> ( J4+ff4 ) i~f (J~+f[.l )

ZJ4 +2(J4+H4)" ZJ- +2(J-+H )2

B3

Tensile stressduc to bending,psi

s( 1= ~tP

4

S(59) = W,+ra Shear stress duc-'

707H )4 Bio= tols10n~ Psl

. 4

H4

BONNET BOLT PATTER%

Fi gur t. 8

0)cl glor i~lount1nq Anal 's)s

k. Shear tear out OE oper Itor bolt head throu<il1 adapter pea« ~

)

S (60) = (hl,+hl~) Y4 r.,2(V14+V2 +V~-+Yq )

5.2 DST5

l. I|caring stress of operator bolt on l1olc in adai1tcr

plate.

S(gQ = ~2(M +T ) + (F + F 2)~.X y

H7

8 T5 DSm. Combined stress in operator bolts., (Scc Figurc 10)

)(6 ) = ~66 ) 'Sf 6 ) ))))6), ))) ) ))'l)))6, .)66;) ')',:. 2 2

lfhere

S(63 = F.A7

Direct tensile s tress, 'psi

S( 6q = PI,.+hl.)Y2(Vl +Y2 +Yg +Yg"')A7

S( 65) = (F~2~1:) 2)-'

nS

= Tensile stress duc tobending moment, psi

= Direct shear stress, psi

'S(66) = (M-..TS)

~

'.5 H S As

Sllca1' t1 css clue to,to1 sion,

ps'.

Bonnet Stresses.

Tllc bonnet s 1'csscs are calculated '~'I tlat tl1c «ssv::~l>ticn

tllilt load11lg 3. s tillougll tllc bo 1 t conllcc t'Lons as p1 c v ious t

)'efined.

c-P

H7

. Y2

oP~R~To~ BOI.T PATTERN

I:igurc 9

~ 0 crator illountlnv. Analysis'

a. The maximum combined stress in thc bonnet was calculated

using the following formulas:

S(67) = S(68)+S(69) ((S(682)+S( 69) ) 2+ i (S(70)+S(71)) )-2 2

Combined stress in bonnet body.

S(68) = Fz+h'4gz

Bg

S(69) = bl~BB + ~l>,B9

(2 '2

Direct TensileStress, psi

= Tensile stressduc to bending

~ moment, psi

S( PPg— (F 2+F 2) ~2 ~ )(4 (g 2+(7 2) ~2 Direct'shear

stl ess 2 psl

FeS(.71) = (t'Iz+T8) (B82+B92) '.

I 2+ Il= Torsional shear

stress

b. The maximum combined shear stress in the bonnet mounting

plate to bod> welds was calculated usi»g the followingformulas;

... Bottom Bo»nct l~'eld

s(72) = s(72) + (s(73)2+6 s(76)2)i„= combinecl she.".r sr ssss2 in bottom weld, psi

WhereI

S ( 73j = S ( 74).+S(75'>

S( 74:)= Fz+K4 g„

Ul

Total tcnsilc stress,ps 1

Direct tens ilc s tress,ps'

0 c r' L 0 r i~loLrn t 1 I'r p, Alla 1' 1 s

+ H

Z2

Bonding tc»sile stress

$ (76) = $ ('g]+$ (78 Total shear stress

S(77:) = (F< +F 2)'~+b'4(g>2+g>.2)'~

.Ul

Dr,1 cot, shearstress, psi

$ (78 ) = (Hz'TS)23

Top Bonnet Weld

Torsional shear stress, psi

$ (79 ) = (S( 80) +4S(83) ) = Co)rrbi.ncd shoar stress in'''

2 2

2 top bonnot reweld

%here

<' S ('81)

'S( 82)

Fz

U2

i~f~.

Z I Z2

S(.80) = S(81)+S('82) = Total tensile stress, psi

Direct terrsilc stress, psi

Bending ter>s i le stress., ps i

$ (83) =

S('84) '=

S ('84)+S (8$ )

(P. Fij'2

Total s)lear stress, psi

Direct shear stress, psi

s(ss) = ii,+'rq = Torsional shear stress, psi

~To Trunnion A~ssombl

. The top trunnion assembly consists of the top trun-nion plate, the top trunnion, the wclds, and the body

material immediately adjacent to'he trunnion. Figure 10

illustrates the elements of the assembly.

1. Combined shear stress in the top trunnion platewelds is a maximum due to seismic and torsionalloads+

S(86) = (S(87)2 ~ S(88)2)<

Nhere:

(87) = '4 (hfx2 + "hf 2) 4 + F~ '

.707(. )

Shear stress due to operator eccentricity.S(88) = 4(Mz+T8) (3311+2T11)

3 l.. 11(Dll+2T11)

Torsional shear due to operator eccentricityand operator torque.

2. Combined stress in base of trunnion body due to combined

bending, torsion and seismic loads.

S (89) =S (90) +S (91)+ ( (S (90) +S (91) ) +4 (S (92) +S (93) ) ) >

Whore:

S(90)-(F + W4g )

2.. 25m'(Dll -8 )

2 2Direct tensile stress, psi

S(91)=32((hT +F K6) +(iV +F K ).x y y x

"(Dll" - a 4)

1)-'= tio))ding tensile

stress, ps i

FIGURE 1O

TOP TRUNIOH ASSEtSLY

Trunion Plateyi,rely

Kg

)+igloo;ino~

Bore

Trvnion Plate—Trunion

Trun ion Base

V«el'g.

4g'-pt'ociy Shel!

S(92) (F 2 ~F 2q< + W (2 2><

gy ' Direct shear stress, psi~ 5" 11-B, )

S(93) = 16(Mz+T8) D = Torsional shear stress, psi11 -B2 )

Combined shear stress in top trunnion to shell weld

is a maximum duo to seismic and torsional loads.

;S (94) = (S (95) +S (96) )~

Where:

S(95) 4((Mx+FyK6) +(i>i +F K ) )'~ + F2

. 70'7 (. 5) Dll mD L

Shear stress due to operator eccentricity

S(96) = 4(Mz+T8) (3D11+2T11)~1 . 4 l Ll1 (Dl1+ 2T11)

Torsional shear due to operator eccentricity.and operating torque.

FRE UHNCY hNALYSIS

A. Introduction

To calculate the natural frequency of the various com-

ponents of the Triton NXL valve, a model system with a

single degree of freedom is constructed. The individual

components and groups of components are modeled and analyzed

as restoring spring forces which act to oppose the re-

spective weight forces they are subjected to. The staticdeflection of the component is calculated and is related

to natural frequency as:

or

or

Fn = 9.8dy

The analysis details the equations and assumptions

used in determining the natural frequencies listed in the

~ summary table, Sketches are provided where appropriate.

B. Valve Bod Assembl

The body shell, as seen in

experience loading due to the

Figure 1, is assumed to

entire valve weight.

Natural Frequency of the body shell:

Fre uenc Anal sis

Where3

WlL1 hgy = x (1 + ) = dy x (47.87) = .0000144492653

bending

shear 31.2 x l.9 x C . = Maximum dafleouion of body2

3 shell due to valve weight,1 inches

2 J5'OTE: Shear deflection consi-o ~ n dered due to low ratio

of (span/depth) otherwisew = 1.9 = Shape factor (= 2 for neglect.

very thin ring)-'REF.

Where —= 2.6EG

and

BANJO ASSEMBLY„

Figure 2 shows the banjo assembly in the body. The natural

frequency of the banjo assembly is calculated using the following:

9.8 I 2where P = 4W /~DN2 y2 1

Where,9

.371 P D16N

COVER CAP ASSEMBLY

NE

= plate stiffness12 (1-v ) ~

2

= Maximum de flection of disc, at perpen-dicular diam. to the shaftLinchesg

As seen in Figure 6, the cover cap supports the banjo. The

natural frequency of the cover cap is calculated as follows:l

9.8 ~2,FN3 ~y3

Where3(m -1) W2(.5D4 + .125)2 2

16mE T4 m3 2

— max . deflection of cover cap

BONNET ASSEMBLY

Figure 7 shows the top trunnion assembly. The following

assumptions are made in calculating the bonnet natural frequency:

Pre ucnc ~ Anal sis

l. The worst valve assembly mounting position is where

the bending moment is predominant in producing deflection.2. The bonnet is assumed fixed at the top trunnion.

3. The adapter plate is assumed to be integral with and

have a cross-section the same as the component itmounts to.

Natural frequency of bonnet:

FN4= 9.8

)Uhere

hy4 = 1~'3H8 +N4K3 + Ã3ZoH83 3 2

3Ell 2EIl

p

~ ~ I ~

A Galveston 11ouston Company

7031 Grand 01vd„

P,O. Ocx 14609

Houston.7cxa 77021

p13) 740-1143 TCICx 70 2713

A$78ce<s~ ~

19 May 1980

HENRY PRATT COitPANY401 SOUTH HIGHLAND AVE.AURORA, ILLINOIS 60507

ATTEiiTIOi~: iIR. KEN WILSON

SUBJECT: T520B-SR2-12 ACTUATOR TOR UE CAPACITIES

Dear Hr .. Hilson:I

This is in response to our telephone conversation ofNay 16, 1980 concerning the torque absorbtion character-istics of a ~fodel T520B-SR2-12 actuator.

As discussed T-5 actuators, either double-acting or springreturn, are capable of ab"orbing 225,000,1b-ins of torqueat the full open or full closed positions. The maximumtorque absorbtion at any intermediate position between fullopen and full closed should be limited to 125,000 lb-ins.These limitations result from the change in the moment armlength of the scotch yoke mechanism as the actuator movesfrom full open to full closed.. The yolce arras and yoke pinis considered to oe the weakest link in the total actuator.design.

If the dynamic torque figures generated by your butterflyvalve exceed the values, we recommend replacement of theactuator with a larger unit.If we may help you further, please let us hear from you.

Sincerely,

4$R. M. Krauss, P . E.Vice President, Engineering

RMK/cck

LEX 76 2713

P. O. BOX 1(1609, l'llONE P13) 7~01143, l)OUSTOH, TEXA" 77021~ ~

'une 'l3, 1973

Henry Pratt Company'401 Sout)! lli«hlan<l Ave.

~ Aurora, Ill. 60507e

'Attention: Hr, Frank Panzica

ATTACHMENT '5

Sub'ct: llcnry Prat t P. 0. U-18965Bct tis Corp. 1'l. 0. 3-0758'-0Parley Nuclear U»it- lio. 2

~ ~

Dear tlr. Panzica:l ~ '

This is to certify that thc model T-520-SR-2 actuators, serialnumbers 30758-1 thru 30758-8 being furnished on.. thc subject orderarc designed to withstand, without loss of function, the seismicconditio»s specified per Inquiry Iio. SS-1102-50.. Dasccl on a ri«id

uipment static analysis, the stre ed compon nts of 'thc model20-SR-2 actuators are suitable for simultaneously appliedizontal and vertical (3 planes) scisuic accelvr. "'",.". of

(, .>der these conditions none of. thc stre scd corponcnts exceed 70~percent of thc yield strcngLh for any of the actua1:or materials

of co»struction.'lhilc i< is. not practical to calc!ilatc thenatl!ral frequency,. the actuators arc col!sidcrcd to be morc thanadcquatc since the seismic analysis's based on-accelerations1i'hich arc greater tlian three tin!cs thc maximum accelerations showno». the spc ct ra curve s,\

~ ~ ...",l: . l E, gT l( r(r<P~A~AA(T~

R, )$ .. ],rauss, P.Chief E»gi»ccr

~

COO RD I MATINGPRINT

~ rFAo I g( /t o*Tc7

ROUTE.. (N(TIA( DATECIVIL . '

ST A VCT

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SE I SMI C AN/ILYS I S

Setfls Robo,arm AcauatorSpring Re"uc n

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SFISiIIC ANALYSIS

T520-SR2T5I6-SR3

GIHCCT Ol'....:. t

hrVf Al:v N

I N TRO DUCT I ON

Th I s stress avalve- ac?vetosoismlc accelthree perpendeach par?Icultho greatestdirection is

C'alyslsof a Bettts

r covers three areaeratlons of 5g slmutcuiar axis. The d

ar analysis wilt bestress on tho memboshown on tho figure

T520-SR2 spr i'ng returns material ly affected byltanoously appliod in theIrcction of gravity for

in tho direction producingr being analyzed and thldescribing'I~is particular

an Iy Is.The axis of tho unit being analyzed wl I I bo as shown lnFi g.

The maximum seismic load of 5g t n three p I anes s imu I taneous I ywill not affect the operatton of tho actuator nor will Itcause a reduction in the rated output torques, since theactual output tcrques are sufficiently higher o accor.od-tetho affoct of 5g on the spring, rod and piston as"omblyand no significant doformations will occur. The minimumrated output torques for the T-5 uni t during se I srni c exi tati onwith .tho iwo different spring cartridges remain:

SR2: 84,375 In. lbs. ending/l68,750 in. tbs. breal;

SR3: 56,250 in. Ibs, ending/(l2,500 in. lbs. break

A' . ~

t g

I ~ .

T 5.':) -" f32

S"a'Pr.SS LCVL')LS

)'a'I tl)o:; I Sc! sml r CxlA "tu:1'rcr I ". P) Oc.'ur: I''VS' ' l" T tS I.'. '' r1 '';,''8 ia I14a aa"lad

t o f I on ':.'h i I c~l::y.. aut ))) l. Tc rn»;;

~ ~ " '1 ~ ~ J aT'a;al'\ '" ''".ili 'l, ' . a 1 'A

Ci)."..f'OW F,lafT STffr.I D.".af

nr- I- .PA.

ldhTF fa. I AL ALLO)'ihi~ra.c,STA!'"S

STr;;-. ~S

Spr I n(;(:<)rtri Jge,Coqncc+.i on

Tie RoTen=if(Preio350 j

os-

lb. )

5 . ASTI) h I '.>3-07314002Sm62000

26026a

366 AO

Tf c )30Pay,,

0 a

hear

I'toosln".;T h d . S t. e <-) r

5 ASTM hf93"07

ASTa'I A53660"45-I5

~ E'mi&800

.6Sm10200

70'a 92

)

H,on 6 af f'i <JTa) 'a'a I ve1«Own'f a ng

Oo f f Sl':.':r(T. ansverso

Bo it Tl:f:6 I IF.<Pr" I o'~i'0 '".. lb.)

AST'"i AI93-97

'STll A I 93-B7

~ 6) )m18600

2Sm6". 000

T9639

045000

Ho oi s I ra,.Tens ) I a'1 Tf)ruBc I t Hc I 6

AST)li h5360"45„I5

Sm1'r C00 3712

HousThd.(."-r c

f50

inqSh-.ar

I o.".jf. lb.)

ASTil A 53660- f5" I 5'

x .6Sm20)a 00

a

1 263') !

C verConnecfton

Govt>I P i nShear

l2 AISl 87405 ~c

.6Sm3)a 000

T28000

I

Pisfon Mew.r

P I a,te P,ST)a Ac'%Q

65" a'5- I 2Sm

1 7000 4 ga,r .

Cy I i n)fcr Hoop ~ AS ~ V.

6i'.I3Sm

20000T

aa 6 1 3

HOTf): ( I ) A I lo~a~.'> l e Stress S per ASla'=. I l I

USAS Ei'a I 7

(7) .The housing is duct l le iron. S ism

bn C.l on 0 A'S I, I .0 - l 967 300 F.

nI '.

~ ~

a 0) Ia ll.i aa

1a.< V

. It() ~ILi;i, 1iXASr.I': t TIS C.'<" l',!'.

T 5?0 "SR2

STRCSS LEVCLS

e 5g Solsmic Acceloratfon In 3 Pianos Simultaneouslybhllo Actuator ls Producing tlax. Output Torquo

CO!<P Oi'I E t I T STRESSIOEWT.

"RCF. IIATER I ALPG.

STRESS Y I ELO SAFETYFACTO@

SpringCar tri dgct~iounting

Tlo Rods»Tonsllo

Tie Rods-Max.. Shear

ASTW AI93-I37

5 'STM AI93"B7

a71747

T36020

105000.

630/0~ 6S

I ~ 5:I

I ~ 7:I

HousingThd. Shoar

6 ASTM A53660"45"I2

T21909 40000

I.G: I

HousingTo Valvetiountlng

Bo I t Shear" (Transverse)

8 ASTM AI94"07 .6Sy13950 63000

4.. 5 : I

Bolt Tonsion 8 ASTM AI94-B/ (r' I3:I

923S 105000

HousingTensile ThruBolt Hole

Hous lngThd. Shear

9 ASTtl A53660-45"l2

9 ASTM A53660»45-l2

5400 45000

iT2066 40000

8:I

CoverConnoctlori

Pl ton Platot~iax ~

Stre ss

Oottel PinShear

l2 AISI 874045 Rc

I4 ASTMi A53665-45-I2,

31035 112000

7064 45000

3 ~ 6:I

5.7: I

Cylinder Hoop Stross l4 Seismic Effect Hegl lgfble

's I ~ I ~ 1 ~ ~ . i ~ ~

~ ~ ~ ~

i I I ~,

~ I ~ ~

~ o'

~ i I ~

coMI'A.l iI

CK'O. ~ l

I~ T i I ~ A I i~ „~ P I

~ r p ~

~ ~

SCISNIC At(ALYSIS

T520„SR2T5 l 6-SA3

Fig. I

AXIS IOENTIflCATION

~ I i'..~ J."cO,".tp Tlute/LS

DI"TTIS Cot'.P. SC(S(4(C AIIALYSI S

520 SR2T5(6-SR3

C.tlf'' t''I h''ent:V. flo.. !t .a

SUBJ ECT: SPA ( NG CARTR I DGC MOUk'T (HG A(BIALYS I S

The two (2) spring cartridge involved in this analysiare: SR2 (8/l4 l 9335) 52-9/l6" long — 500 lbs.

SR3 (B/M. (0737) 40-(/4" long - 325 lbs.

Inasmuch as the SR2 ls the (onqor and hcavtor of the t~<o

spring cartridges and they both have the same attachmentto the body, It ~III'be used for t(ie following analysts.The stresses resulting from the mass of the SR3 i'.III boless than that of tho SR2.

The maximum moment on the connection ls When the springis compressed and this moment Is used beto~v ~

Tle Bar (t) extends through the body, I.ence sees theaffect of pressure load Fp which is 75~i greater than theaffect of sprino load Fs seen by Tie Bar (2), henco TieBar (I) vtill be analyzod. Rofer to Figs. 2a 4 2b,x, y 4 z denote direction.Tto Rod T..nsll

Fl ~ g Ml

22X

L LI

+ Lz1X

F. = g Ntz" z I

2LI

Tte Rod hoax. Shear:

C(m~) +2 I

T ~ (g2 + o2)Q M2 x "z -. I

2A

2(Fp+F(y) + Ft>+F I z~ Fl

Ar 'rFp" oA

Fly gyHI

Fl Totat Load on Tie B-r (I)A ~ Area Pres. Cyl.p

.= Oper ting Pres. - pstgM,

= ~'eight of Sprtng CartridgeL ~ Dist. to.c.g. of Sprlnc

Cartridge '0 Spring CompressedL'I ~ Lever Arm or Tie Pod (I)L2 . Lever Arm or Tie Rod (2)=A ~ Root Area of Tie Bar Thd.r

h/ax. Shear t n Tie Bar1

~ Tranverse Shear Stress2'i

8 Fl aro forces resultingfrom C moments aroundB or B"

Tc'nsllo (tress ln T(v Bar

g ~ 5~ x

g ~ 5y

g ~ 6z

I mvq i ~.i ~

can. qt ',

SEISMIC ANALYSIS sH(:Ll;LAs7 nr'v t4o

T520-SR2T5I6-SR3

Hous in Thd. Shez r:2F

I

0 L

FiDm'

\

3

Total Load On Tie Bar { I )~ Thd. P 0.

Length EngagementHousing Thd, Shear Stress

The housing is ductile Iron. S ls based on USAS 83I.I.OI967 0 300 F.

SUBJECT: PISTON ASSEMBLY TO BODY CONNECTION

The largest piston assembly covered by th.ls analysis Is a20" cylinder having an assembled weight of 495 lbs. witha maximum moment arm to tho point of connection of l5 inchesproducing a bending moment at Ig of 7,425 in. lbs. whichis less than the bending moment producod by the springcartridge (I4,800 in. lbs.)inasmuch as thc pressure load is The same on the tio rodsof the spring cartridge and tho pressuro assembly andsince the moment for the prcssuro assembly is less thanthat of the spring cartridge, the tie rod stresses forthe attachment of the pressure assembly to tho body wIIIbe le s ,han tha doscribod for the spring'cartridgeanalysis sho~:n ln Fg. 5

~ ~

I h1 l II~ 8 ~

QlgtAI>I I,(l ( r ') I

Cli'O.

~ ~

SC I SI1I 0 CHAL:S I >

T520"SR2T5l6-SAD

CSXKPP A&tWTT

nE B~n l

TlK BAG P,

~ ~

F l g~ 2e

/ ~

I

I ~l

Flg, 2b

4

TlL OAR I'l'iit;.S l S

SE I St11 C AttALYS I S

7520-SR?T5I6-Sre3

(IsHUF.T .'.. Ol . ",. lI

LhsT i{i.v.l~Q,.....

OJ~S

SUBJ ECT: HOOS ING TO YALYE MOUNTING

This analysis refers to the 7520-SR2 which Is heavierand longer than he T516-SR3, hence ha" the largermoun'ting stresses.

Refer to: Fig. 3 - Centor of gravity locationFig. 4 - Actuator mounting flange

'he

various locations "L" and the direcvton of thenGfi forces are assumed as sho'en jn Fig. 4 ~ The sumof these forces produce the maximum tensile loud Inbolt "A"'

u F + F + Ia 'x a az

ArP i

1" L I.Qx gx z 3x

2(L + L +L +L, )lx 2x 3x 4x

QX gZ "-

gy ~ 6

'L< >~ L 'etc"IX+in I x

'g

ML. Lay y 2 4y

2(l 2 +L2 +L2 +I 2 )ly 2y 3y 4y

1'! I L

2(L2 + L2 + L2 + L2 )lX 2X 3X 4X

Shear ln the mounting bolts is produced. by the sum of theactuator output torque and sel mlc affects causingactuator rotat I ona I load. Latera I shear I s absorbed bythe center I ng ra I sed face.

2 LT + ( g y Lx + 9 x Ly

) ~N4

ObNA

T *I p(a)2 + <2 1

5 X'

~ Actuator Output Torqueln. Lb..

Db ~ Bo I t Circle DI am.

N ~ No. of Bo I ts

a ~ Ooft Tonsllo Stressa

Shear Strus '

ta x I mum S I> o a rI

iii ' t, ~

rlF~'I~)'OH, 7 I,'h5

r.'=r TIS CO;:I. SEISIlIC ANALYSIS

T520-SR2T5IO'"SR3

sr ll=.r.."r' I2p.Li'.sT r'il V. t'I3..

F

SUOJ ECT: HOUS ING TEI<S I LE STI'ESS

The housing tensl le stress (o ) through tho mounting2

b9 I t ho I o at max lrnurn output torque and se I sn I c a f fects I s:

0 I- 22

DbHh I,

tT + (g L g..L >lip

,Al ~ (I .563 - .75) = StressArea of Housing (! I"Engagement

~ ~

SUBJECT: HOUSING THREAD SHEAR

~" 2«ax Fav + Fez>

xD LF

0

Dz Thread P.D.

L ~ Length Engagemont

Houstng ThreadSlronr Str ess

I FF

~ F ~ ~ ~ ~ I ~ ~ .

~ ~ ~ ~ ~~ ~ . . ~ . ~ ~ ~ I

rFF ~ F I

~ ~I I,. F < FF

IF IF ~ ~ ~ ~ I I ~ ~

F I ~ ~ F

1~ I

~ I ~ ~ ~ F F,I I ~ ~, ~ I

~ rF ~ ~

SElS:.;iC h in(..',"iS

1'5PO-SR2T5lG-SA3

. I{I.I.T ... C'

A~wV llCV. IIO....;

cJ'I

r

Y

IJl

I

I .i~—I—I

i'

/ /I

T520-GP2'SAD

'l65870

III

Lx-t. 5604 ~ 300

Ly8.4297.260

I

Lz;.660

.,v'.630

Fl g, 3

CFNTi 9 0,

s

II$ ~

rn o,

I ~

lr'r(JU.rTGr'gr Tj:X's$

SCISIllC ANALYSIS

~0SR'5I6-SB3

—Q

YIAX,SHEAR 6)(~7

I'C

I

DIRECTION OFGP.;.VITY

Flg.

tlOUHT I N G FLAIIGEANALYSIS

I

~ ''

~ W

SE I SI11 C ANALYS I S

T520-SA2. T516-SRB

SH):l.:T . 'r...'2:i:t AOT AVV. t:~5

SUDJECT: COVER CONNECTION

Tho twelve (12) hex hoad cap screws on tho cover aro fortho tension only. Tho shear load" from tho piston andspring roactions are carried by the dowoI pins. in thefoIIowing analysis, ,ho dowel pins are assumed to carrythe entire load without benefit of clamping force fromthe retaining screws.

Tho maximum force nominal and equal to the thrust of the. piston occurs when the yoke Is at 0'r 90', That is,45'n either side of the nominal centerline of the body.

Tho maximum seismic offect on the cover connection willoccur with 5g acceleration along the Y axis utilizing thomass of tho spring, piston and piston rod assemblycombined with a 5g accelera,ion along the X axis utilizingthe cover and yoke. This analysis is shown in thefollowing Fig. 5: and equatio'ns. The total pressure loadis absorbed by the body and cover equally, hence the force(Ft) in the following is half Ihe pres uro Io-d. Frictlonaf.losses are not considered in that they "„',ould reduce thestross values on the pins.

At i;Oa

By EHa

T6 ~

Shear stress innormal operation

Ft ~ I/2 p-iston thrustRbx " I ~F L FnL + FtL ~ load.

X L n 3 n

0

Rax - RbvF ~ Norma I Ic "d

(Fn Ft t.'-0 8 90 )

f (R~„0~ + (Rhx) 3Cros"ectlonal aroaof pin

~At 5

I+ (g>+g ) z>l7 6 x y

4A

Combined weight ofspring, piston's, pi tonrods, yoke 8, cover.

'C Shear stress P.

maximum so i smi c,

SE I SHI C ArlALYSI S

7520"SR2T5IG"SR3

Li

4 5eS

FI g; 6

COYER CGIINECTIONANALYSIS

~II

~,

SC. I SVii <'N XLvS I ss

T520-SR275I6-SR3

~ I

srir;i:."i ...'"'r ' ."., I

i As'r rrr:v.:r<.) ..!

w~~'uuuM~~ 4

SUBJECT: PISTON PLATE STRESS (a )3

Tho maximum p I ato stross occurs at maximum oporatlngprossuco <l00 p"ig) added to Gg acceleration. Platehas Inner edgo fived at hub and outor odgo froeuniform pressure.

a"(m+3)+b4(m-I)+4a2b2g3 <p + p ) C4, 4 <m+ I ) Log„

4~ 2 a (in+I) + b (m I)1

~ P I a I e thi ci:ness at hub

p ~ Equivalent seismic9 prauuuro (uTIBY

A.a ~ Orator radius

b ~ Hub radius

m ~ Reciprocal of Poisson'sratio

SUBJECT: CYLINDER

Tho hoop stress (a ) at mo>:imum oporatlng prossure ls4affected virtual ly none by 59 sotsrnlc ovitation,

0

tR ~ Insido radius of Cyllndor

t ~ Thickness of cyllndor

I ~ I ~

. ~

P'P,'