ISOLATION/PURGE VALVE ANALYSIS FOR
'6"-12pp BUTTERFLY VALVE
Project Site Susauehanna S team Electric Station Berwick Penns lvania
Customer Penns lvania Power 6 Li ht Engineer Bechtel Power Cor oration Specification No. 8856 Original Purchase Order 8856-P-31-AC Original Pratt.Job No. D-0026»3
Valve Tag Nos. HBB B AO- 721
General Arrangement Drawings C-2600 Rev. 5
Cross Section Drawing C-2988 Rev. 2
Prepared by: Date:. >gglllftt'ttff Reviewed by: Date:~- Certified by:~ Date:
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J t ll PI/i lcm CONTENTS
I. Introduction II. Considerations III. Method of Analysis A. Torque Calculation B. Valve Stress Analysis C. Operator Evaluation IV. Conclusion V. Attachments (1) Input Documents (A) Pressure vs. Time Graph Customer/Engineer Response to Request ~o 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 C valves dixring a faulted condition arising from a'loss of coolant accident (LOCA). The analysis of the structural and operational adequacy of the valve assembly under such conditions is based principally upon containment pressure vs. time data, system response (delay) time, 'piping geometry upstream of the valve, back pressure due to ventilation components downstream of the valve, valve orientation and direction of valve closure. The above data as furnished by the customer/engineer forms the basis for the analysis. Worst case conditions have been applied in the absence of definitive input. IX. Considerations The NRC guidelines for demonstration of operability of purge and vent valves, dated 9/27/79, have been incorporated in this evaluati.on 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. t 2. Plow direction thr'ough 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. Horst case is determined as a single valve closure of the inside containment valve, with the outside containment valve fixed a't 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. ~ ~ ~ < ~
7&8. Drawings or written description of valve orientation with respect to piping immediately upstream, as well as direction of valve closure, are furnished by customer/engineer. In this report, worst case conditions have been applied to the analysis; namely, 90 elbow (upstream) oriented 90 out-of- plane'ith 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 of the valve components indicating if,the stress levels under combined seismic and LOCA conditions are less than 90% of yield strength of the materials used. A valve operator evaluation is presented based on the operators ability to. resist the reaction of LOCA-induced fluid dynamic torques.
C ~ Sealing integrity can be evaluated as follows: Decontamination chemicals have very little effect on EPT and stainless steel seats. Molded EPT seats are generically known to have a cumulative 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. Method of Analysis Determination of the structural and operational adequacy of
) the valve assembly is based on the calculation of, LOCA-induced torque, valve stress analysis and operator evaluation. A. Torque calculation The torque of any open butterfly valve is the summation of fluid dynamic torque and bearing friction torque't any given disc angle. Bearing friction torque is calculated from the following equation: TB=P xAxUxd where
P =pressure differential, psi A = projected disc area normal to flow, in2
U = bearing coefficient of friction d '= shaft diameter, in. Fluid dynamic torque is calculated from the following equations: For subsonic flow
~ CR — aPP P2
3 T = D x D CT1 x P2 x F~ For sonic flow
Pl RCR P2
3 T = D x x P2 x K x F D CT2 1,4 RE (FR — 1) Where T = fluid dynamic torque, in-lbs.
F~ = Reynold number .factor R = (f (~) ) CR critical pressure ratio, P = at flow condition, psia 1 upstream static pressure P = downstream pressure at flow condition, psia 2 static D = disc diameter, in.
C subsonic coef icient Tl1 torque f CT2 = sonic torque 'coefficient K = isentropic gas exponent ( —1.2 for air/steam mix) 0 0 = disc angle,-such that 90 = fully open; 0 = fully c'los ed
C and are a function of disc angle, an Note that Tl1 CT2 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 pr'edicted 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 coincident~ ~ with a disc angle of 72 (symmetric) or 68 (asymmetric) from the fully closed position.
The following computer output summarizes calculation data 0 0 and torque results. for valve opening angles of 90 to 0
D-34933(D0026-3) TORQUE TABLE 1 3 / 10 / 82
JOBtSUSQUEHAHA/BECHTEL SAT.STEAM/AIR MIXTURE WITH 1.4 LBS STEAM PER 1-LBS AIR SPEC.GR.= .738255 MOL.WT.= 21.3872 KAPA(ISENT.EXP.)= 1.19775 R= 72.1972 GAS COHSTAHT-CALC. SOHIC SPEED ABSOL;MAX.TORQUE(FIRST SOHIC)AT 72"68 DG.VLV.AHG.= 478 IH"LBS e 68 DEG. MAX.TORQUE IHCLUDES SIZE EFFECT(REYHOLDS HO.ETC)APPX. X .996595 FOR 6 IH CH BASIC LIHE I.D. ALL PRESSURES USED:STATIC(TAP)PRESS.-ABSOLUTE)P2 IHCL.RECOVERY PRESS. (TORQUE)CALC'S VALIDITY:Pl/P2)1.07; VALVE TYPE: 6""1200 CLASS 150 DISC SIZE: 5.2 IHCHES OFFSET ASYMMETRIC DISC SHAFT DIA.: 1 INCHES BEARING TYPE!. BROHZE SEATIHG FACTOR! 15 INLET PRESS.VAR.MAX.: 48.2 PSIA OUTLET PRESSURE(Ph): 17.2 PSIA (72 DEG. ACTUAL PRESS. ONLY(VAR.)) MAX.AHG.FLOW RATE: 6658.94 CFM; 7698.92 SCFM; 423.231 LB/MIH CRIT.SOHIC FLOW-90DG: 518.53'? LB/MIN AT 19.651 IHLET PSIA VALVE IHLET DEHSITY: 6.35583E-02 LB/FT"3-MIH..129262 LB/FT"3-MAX. FULL OPEH DELTA P: 7.74903 PSI SYSTEM COHDITIOHS: PIPE IN-PIPE-OUT -AHD- AIR/STEAM MIXTURE SERVICE 8 265 DEG.F MINIMUM 0.75 DIAM. PIPE DOWHSTREAM FROM CEHT.LINE SHAFT. Pl ABS. PRESSURE(ADJ.)FOLLOWS TIME/PRESS.TRAHSIEHT CURVE ~ "-5 IH.MODEL EQUIV.VALUES-""""-ACTUALSIZE VALUES"—-- AHGLE Pl P2 DELP PRESS. FLOW FLOW TD TB+TH TIME(LOCA) APPRX.PSIA PSIA PSI RATIO SEATIHG + BEARIHG + HUB SEAL TORQUE (M/M)= 628 IH-LBS e 0 DEG. MAX.DYH. -'EARIHG " HUB SEAL TORQUE (M/M) 489 IN-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 formula: Smax = 3: (Tl+T2) + 1 (Tl+T2) + 4 (Sl+S2) 2 2 where Smax = maximum combined, stress, psi Tl = direct tensile stress, psi T2 = tensile stress due to bending, psi Sl = direct shear stress, psi f S2 = shear stress due to torsion, psi The calculated maximum valve torque resulting from LOCA conditions is used in the seismic stress analysis, attachment, 02, 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. CD OPERATOR EVALUATION Model: Bettis 521C-SR 60 Rating: 7,000 in-lbs. at full open and closed positions only. 4620 in-lbs at 68 4000 in-lbs at 45 (minimum rating) Max. Valve Torque: 628 in-3,bs. 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 absorbtion rating of the operator, it is concluded that the Bettis models furnished are structurally suitable to withstand combined LOCA and seismic 3:oads. 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 lA PRATT PROPOSAL LETTER H:HmH.V x aWTT Carvrxwwv (:t'0;ltii'( ( ll'"ill(( ~ I ill~~ i()I I illi(l~.silt..'Ills 401 SO%I'H EIIGHLANDAVENUE ~ AURORA, ILLINOIS 806'pril 16, 1981 Bechtel Power Corporation Box 396S '.O. San Francisco, CA 94119 Attention Mr. E.B. Poser .. Project Engineer SUBJECT: Susquehanna Steam Electric Station - Containment Xsolation/Purge Valve Analysis" Gentlemen: 'ith reference to your recent inquiry regarding suitability of the valves and actuators to withstand aerodynamic, LOCA conditions, please note the following: 1. 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 coe ficient for all ventilation svstem components downstream of .*- the valve (one for'each valve size) or A graph of back pressure vs. LOCA time at a distance 10-12 diameters 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 t'imes fiom LOCA to i.nitiation of valve rotation. E.. Drawings or written description of valve orientation 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. Bechtel Power Cc. adoration Page 2 April 16, 1981 -'PATT) q; ~ In the absence of'he above information, the following asstqnp- tions will apply to the purge valve analysis. 1. Back pressure of 19.7 psia throughout valve closing cycle. Higher back pressure increases maximum dynamic torque and valve stresses. 2. Delay time from LOCA to initiation of valve rotation shall be chosen to permit initial sonic flow condi- tion and critical valve disc angle to coincide, resulting in maximum possibl'e 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 actuatoi supplier will be asked to veri y the suitability of the actuator for the reaction or back drive force resulting from aerodynamic torque conditions. 3 ~ The cost of performing the evaluation of the valve components will be $ 12;800 each size "or 6", 18" 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 demonstrating operability 'of purge valves is included in the analysis. This proposal is Nor investigative analysis only and is not intended to guarantee the adequancy of the equipment as fur- nished when subjected to LOCA loads currently being defined. The proposal 1s valid for thirty (30) days. The terms of payment will be Net 30 Days. He hope you will find the proposal responsive to your needs. Zf we can be of any additional assistance in this matter, please advise. Very truly yours, HENRY PRATT COMPANY ~ /le*~. Glenn L. Beane GLB/tl ~ Manager-Application Engineering ATTACHMENT 1B CUSTOMER/ENGINEER RESPONSE TO REQUEST FOR INFORMATION gpPt fIP.",Yf.QF) F~"~~3~~~ 8echtel Power Corporation Engineers-Constructors Henry Prat t Company. Beale Street 401 South Highland Avenue San Francisco, California 'ifty P.O. Box 3965. San Francisco. CA 94119 Aurora, Illinois 60507 Mal(Address: Attention: Mr. G. Z. Beane '15'r J."tl 1 'god(f Subject: Susquehanna Steam Electric Station Units 1 and 2 Job 8856 P.O. 8856-P-31-AC, Containment s'e Isolation/Pu e Valve Anal sis gQ Gentlemen: 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 temperature time curve is attached. C. A back pressure of 19.7 psia should be used in this analysis. This back pressure is per the assumptions in your letter of April 16, 1981. D. Minimum delay time is O.l seconds. Maximum delay time is 5 seconds. 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 unqualified, 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 I' 0 Mi'/I~ ( Hg 502d Qp ~g I C ORYWELl WETWEt.L 20 m n m D 2 I= m 10 I x m I CO CD Cn TI a !Il C ID I tO m~ m R r. n CQ c2m m I" TITHE tlec) M ' R ORYWELL IL O W CC', I K CL, I- ~ SUPPRESSION POOL m m C n a m 100 n Z ' C x r I CO Z CD mC~ Z Ol ~<+m CD m >~m m I t5 a It t.O +5)$ 5 r I I p+ r'laII55D ltH +'c. 5 0 ~.1 S tl III H "5'55 ' ~ REFERENCE ' DNNNGS NtI$7 SII.7 Crt.4 tatgl.Ct. 0 fCAVt4CC4 "' ~ AftNftj l7 ArlW f7 h F C7o 5d N ~tttttttttttttttI llO ltIPN WllaOIL~ ILC4'9 t t ~ 5 rett.t COMPONENTS ON I ~ ~0 tt ~ ~ lt lte TIIIS DNG. ARE G.LISTED SPEC. I856.G-S APPLIES ffNNSTLVANIA7018KN h LICH'OItIFANT taaaetaee,nttttat~t 0%4Uotaatta ttaatt talllac ttatttta atit a.lrst t ~ttttttL aatattaatttalco /SOHf 7'PIC ~ RCttCÃOR dlIOa7. CdtI74IIV&tIIFIf'Atda. 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ARE ~c«e 0»00» tote»,»II 'e« SPEC. 8856-G-9 APPLIES 0 D PNNSYLVANIA POPOVER R LIGNf Cbh1PANY ~ « olIIcc Ic«0 ~ Iooc c I 'Ie« 0 Ccdvlccee«e III»0~ call«allo»00 eccl ~.Itef ~ D D ICC'111 late l»lot»OCICO fc ca ~ ct I StfhfaM IC RCAC TCR dLOf'0 ~ coNfkwcaftivr A2'ccfo5, cdt»fttoc ~ vent»T I ct ~eto 51 f ~e CCOC»CKCC $ 85$ tIaa-Ii8.f 7 ~t ' 1r Itt ~ REFERENCE DRANHGS hf tlSTMI teA! Nfl& ~ i T pate mW-Waem ~ tt ~tCttà tCC tIQCCC %4 Atttt crc tvrtdtl ICt tttC(0 f(4 ICCCKtttr ~IIr ~ COMPONENTS ON ~ttt (It ~ I~ THlS DWG. ARE G-LlSTED SPEC. 8856-G-9 APPLIES NNNSTLVANIAPOWER P UGHT COMPANY itttatrrKttIWttvttt~ ~trrttttwtltttwttlcttKttkfnetwit twtt ctcnttc cttttrAttcttco 0 /50hfR TRIG-REiKT~ EKO6. awruww1Ekl'byss.coAITRx- QvlP g WK 5 ~tV PPEEG !SSI kg- ~I~- ~ 3 nln K-an C v C CI 4I j»5 4I e.' «5V (; »~ ~ C .r V r 4 gayt ~P) K / v »C ao VU aa C Iig jgP'aa Ca O g((o Bc 2'r »CCD CD ~ 8 foo.o'A4LCA. 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CONTAIHHNT ATIII.CONTROL - UNIT I ~ ~a I5 C~ N Q HBD- IIII -I 2 ett OetahtKta W tttr Wttt g2 8 "b , 2 A A' i I Ne rrg a t e ct V N~ At P t s ~ ~xaam jH .-„(~ IL S I') e1 erC ~s ~-'S/ 'O COO e2 e Ce REFERENCE DRANlNGS I ISO SCS t! g gp /g pybtt.lt Cg At t57 5r./ SYCK 4 Rf /.O. rC ~ At.h'f S r rirWOruti ASC/1 e // E tf AV D Tc rt E'K CL e CL r L Ve e e Se E~ Art CCA O, IAC e et' L ta' ct ~ alee rA wc I C e at~I' CCC ~a ILKI Ic&)e ~ AAA ~ 'e e ta J /:,t 'CLCO CCO SASSCASSOC ~ t COMPONENTS ON ~ C ~ ~ 5. ~C CCCI ~ t 'e erect 'at ~ CC eC e THlS DIIG. ARE 0-1.lSTED e hc ca tart tear ~ICt O SPEC.,8856-0-9 APPUES PENNSYLVANIA PO)YEII 5 LIOHY COMPANY O e ~r Alslatoacctlercltaet ~wovllcaaaa ~ IIANIIIIIAK~ Ialcor ItrlAcctll ~ CANIOANCISCO ~L ICNSCC I /5OHC MIC /tfrtgTOR eADG. GgrvfrtirtACCAIC'CFAf05 CoAIMCSC, t/AII/ t/ reaa 57 + ~ca et g~t o s AT ctV g ssss //e e -//e -/ 5 ~I,I aoa aaooa 's Ice V IV M CcCC c: ATTACHMENT 2 EdumIImmtI KCv'~~a 9K l SEISMIC ANALYSIS FOR 6 INCH C NUCLEAR PURGE VALVE TABLE OF CONTENTS ~Pa e k List of Figures 2 Nomenclature 3 I Summar Tables Stress Level Summary 20 Frequency Analysis Summary 24 I Valve Dimensional Data 26 Stress Analysis Introduction End Connection'Analysis .32 Body Anal'ysis 33 Disc Analysis 39 Shaft Analysis 42 Disc Pin 44 Analysis'ha ft Bearing Anal'ys is 45 ~ 'over Cap Analysis 46 Thrust Bear'ing Analysis 49 Operator Mounting Analysis 50 Frequency Anal sis 59 / ~ LIST OF FIGURES Ti.tie ~P'a e Valve Body Spatial Orientation , 2p Valve Cross-Section r31 Pressure Area Analysis Cross-. 34 Section in Crotcli Region / ~ Pressure Area Analysis Cross- Section in .Body Disc 40 .Bottom trunnion Assembly 47 Top Trunni'on Mounting '1 Tr'unnion Bolt Pattern Bolt Pattern S3'Bonnet ' V NOMF.NC 1 A'TURI! The nomenclature for this analysis i's based upon the .nomen- clature established in paragraph NB-'3534 of Section III of the ASME Boiler and Pressure Vessel Code. Nhcre the nomenclature comes directly from the code, the reference paragraph or .figure for that symbol is given with the definition. For symbols not. IP 1 defined in the code, the definition is that assigned by Henry "I Pratt Company for use in this 'analysis. -p ANALYSIS NOhtENCLATURE Effective fluid pressure area based on fully corroded interior contour for calculating crotch primary mem- brine. stress (NB-3545.1(a))',in2 hfetal area based on fully corroded int'erior contour effective in resistin'g fluid force on Af (NB-3545. 1(a) ) j in A3 Tensile a'rea of cover cap bolt, in2 A4. Shear area of cover cap bolt, in2 A5 Tensile area of trunnion bolt, in A6 Shear area of trunnion bolt, in2 A7. Tensile'area of operator'bolt, in A8 Shear area of operator bolt, in Bl Unsupported shaft, length, in. \ B2 Bearing bore diame'ter, in. QO,'g Bonn'et bolt tensile area, in2 B4 Bonnet bolt shear. area, in B5 Bonnet body cross-sectional area, in ,B6 Top 'bonnet weld size, in. B7 B'ottom bonne''t weld size, in. ~ B8 Distance to outer fiber .of bonnet from s'haft on y axis, in., Distanco to outer fiber of bonnet from shaft, on x axis, in. A factor depending upon the method'of attachmen oK head, shell dimensions, and other items as listed in NC-3225.2, dimcns'ionless (Fig. NC-3225.1 thru Fig. NC-3225.3) Cb Stress index for body bending s'econdarv stress re- sulting from moment in connected pipe (NB-3545. 2 (b) ) . Cp'' Stres. index for body primary plus se'condary str'css, illsido surface., resulting from internal pressure (NI~-3545.2(~)) -4- ANALYSIS NOhlENCLATURE r, Stress index for thermal secondary membrane'. stress resulting from structural discontinuity C3 Stress index for maximum secondary membrane plus bonding stress 'resulting from str'uctural discontinuity Product of Young's modulus and coefficient of linear . thermal expansion,'t 500oF, psi/oF (NB-3550) C7 Distance to outer fiber of disc for bending along the shaft, in. C8 Distance to outer fiber of disc for bendi:ng. about the shaft, in; C9 Distance to outer'iber of flat plate of disc foe -'ending. of unsupported flat plate, in. ' Inside diamet'er of body neck at cro'tch region.(NB- 3'545;1(a)), in. dm Inside diameter used is basis for determining body minimum ~; all thickness, (NB'- 3541), in. Dl Valve nominal diameter, in; D2 Shaft diameter, in. 'D3 . Disc pin diameter, in. D4 Thrust collar ou'tside,diameter,,in. D5 Spring pin diameter, in. Dg Cover cap bolt diameter, in. Trunnion D7'8 bolt diameter, in. 'Operator bolt diameter, in; Dg Bonnet bolt diameter, in. hfadulus of elasticity, psi Fb Bonding modulus of standard connecting pipe, as given by Figures NB-3545.2-4 «nd NB-3545.2-5., in> 1 Fd 1/2 x cross-.sectional a:oa of -standard connected pipg, as g'iven by Figures NB-3545.2-2 and NB-3515.2-3, in.4 Natural frequency of respective assembly, hertz -5- 19 .< ANALYSIS NOMENCLATtJRE Fx. .tf3gx--Seismic force along' axis due to seismic '' acceleration acting on operator exte»dcd mass, pounds IU3gy--Seismic force along y axis duc to seismi.c acceleration acting on operator extended mass, pounds lf3gz--Seismic force along z axis due to seismic acceleration acting on operator extended mass, pounds 'ravitational acceleration constant; inch-per-second2 l * Valve body. section bending modulus 'at crotch region Gb'd (NB-3545. 2 (b) ), in3 Valve bogy section area at crotch region (NB-3545.2 (b) ), in :Gt Valve body section torsional modulus at crot'ch.region (NB-3545.2(b))'; in> gx Se'ismic acceleration constant along x axis Seismic , Ry acceleration constant. along y axis I ( Seismic acceleration constant along z axis * hg Gasl'et moment arm, eq'ual to the radial distance from thc .centerline of the'bolts to the line'.of the gasl'et reaction (NC-3225), in. Top trunnion .bolt square, in. H3 Bottom trunnion bolt square, in. Bonnet bolt square,. in. H5 Operator bolt square, in. Bonnet bolt ci'rcle, in. I Operator bolt circle, ill. Bonnet height, in.'ody Acti.lal Mall thickness, zn. Bol'lllet bocly mome»t of illcrt3a about x axi,s, in4 I2 '. Bo»n'ct boil) Moment of i»crt i a about y axis, in4 73 ])isc a rca mome.'.»t of i»cl'tia. for bonding about t.he shaft i»4 19 ANAI.YSI S NOhl)lMCLATURE Disc area moment of inertia for bending along the shaft; in" hfomcnt of inertia of valve body,, in4 hfomcnt of inertia of shaft, in4 I7 Disc hrca moment. of inertia for bonding of unsupported flat plate, in" ' Distance to'neutral bending axis for top trunnion bolt pattern along x axis,'n..' 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.'istance .J4 to neutral bending axi's for bonnet bolt pattern along y axis, in. '! Distance to neutral-bending axis 'for operator bolt, ppttcrn along x ax'is, i'. 'istance to 'neutral bending axis- for operator bolt pattern along y axis, in. '. / Spring, constant / Kl Distance of bonnet leg.from shaft centerline, in. ! / K2 Thic)'ness of disc above shaft, in. KZ Length along z axis to cg of bonnet plus adapter plate asscmbl>, ig. K4 . Top trunnion».id'th', in. ! KS Top trun»ion depth, in. K6 ))eight of top tru»»ion in. ! Ll Valve body face-to-face= dimension, in. Lp Thicl'ness ~ of. operator housi»g under trunnion bolt, in. Length of e»gagcmcnt of cover cap bolts in bottom Lg'e trunnion, in. '4 Lcngt)1 ol c»gagcmcnt. of tru»»ion bolts i'n top trU» lli011 in . ANALYSIS NOMENCLATURF. L5 Scaring length, in. L6 Length of structural disc hub welds, in. Lp Length of engagement: of bonnet bolts in adapter plate, in; Length of engagement of bonnet'olts in bonnet, in. Lg Length of engagement'f stub shaft in disc, in'. e Reciprocal of Poisson's ratio h Mass of component hfx '.Wg(gyZo+gzYo), operator extended mass seismic bendin'g . moment 'about the x axis, acting at th'e base of the 'perator, in-lbs.. hiy MZ(ggZo+gzXo), operator extended mass seismic bending moment about the y axis, acting at the base 'of the . 'perator; in-lb's. - Mz l'7>'(gxYo+gyXo) operator extended mass s e ismi c bending .g moment, about the z axis, in-lbs. Rx Wx+FyT5, operator extended, mass seismic bending moment about.t)ic x axis, acting at the bottom of the adapter '. plate,.in-lbs. My+FxT5, operator extended mass seismi'c bending moment abou't, t)ie axis, acting at the bottom of the. adapter 'late, in-lbs..y hfx+Fy(T5+H3)+gyN4Kp, operator extended mass seismic bending moment about the x axis; acting at the base of the bonnet, in-lbs; . I ly h|y+Fx(T5+llg)+gxN4Kg, operator extended mass seismi;c bending moment about the y axis, acting at thc base of .thc bonnet, in-lbs. h)8 Bending moment at joint of flat plate to disc hub, in-lbs. Na . Permissible number o'f complctc start-up/shut-down . cycles at hr/100oF/hr/hr fluid tcmperaturc change rotc (Nll-3545.3) Not applic.".blc to thc analysis of thc system v. Nl Number of top disc pins 19 7- ANAI,YSIS NOMI:NCI.ATURI! N'2 Number of. operator bolts N3 Number of trunnion bolts Design pre's sure, ps i .pr Primary pressure rating, pounds ~ ~ 'Ps calculation pressure from'tandard Figure .NB-3545.1-1, psi 'argest value among Peb, Ped, Pet, psi Peb Secondary stress in crotch region of valve body caused . by bending of connected standard pipe, calculated according to NB-3545.2(b), psi Red Secondary stress in crotch re'gion of valve body caused by direct or ax'ial 'load imposed by connected standard ..piping, calculated according to hB-3545.2(b), psi r Pet. Secqndary stress in crotch 'region'f valve body caused by twisting of connected 'standard pipe>-calculated .according to 4'B-3545.2(b), psi Q." p 'eneral primary membrane stress i~~sity at crotch region, calculated according to NB-3545.1(a), psi Pm i ,Pri'mary membrane stress.intensity in body wall, psi Qp Sum of prim'ary plus secondary stresses at crotch resulting from internal pressur'e, (NB-3545. 2 (a) ), psi \ 'I . Thermal stress in .crotch region result'ing'from 100 'T'T1 F/ hr fluid temperatu're change'rate, psi hfaximum thermal stress component caused by'through wal'1 temperature gradient associated with 100oF/hr ~ fluid temperature change rate (NB-3545.2(c)), psi I ~ QT2 Maximum thermal secondary membrane stress resulting * from 100 F/hr fluid temperatilre change rate, psi QT3 Maximum thermal secondary membrane plus bending stress resulting from structural discontinuity and '00ol:/hr fluid temperature chango rate, psi h5caii radius o'f body wall at crotch region (NB'-3545.2 (c') -1), in. Insicle ra'lius nC 'body at crotch region for calculating 35'45. Qp (NB 2( 1)) p in ANAI;YSI S NOVI!NCI,ATURE rg Fillet radius of ecternal surface 'at crotch (NB-3545.2 g (a)), in. Dis'c. radius, in. R5 Shaft radius, in. Mean radius o f body wall,'n. 'R6 Radius to O-.ring..in cover cap, in. S Assumed n>aximum stress. in connected pipe„ for calcu- lating Pe (NB-3545.2(b)), 30,000 psi Sm Design stress intensity,'NB-3533), psi . Sum of primary plus secondary stress intensities at- „ crotch region resulting from 100oF/hr temperature change','ate (NB-3545.2), psi " Spl Fatigue stress intensity at inside surface in crotch region resulting from 100oF/hr fluid temperature change rate (NB-3545..3), psi Fat'igue stress intensity at outside surface in crotch region resulting from 100 F/hr fluid temperature change rate (NB-3545.3), psi S.(1) through S( 71) are listed after the alphabetical section. r te 'Minimum body wall thickness adjacent to crotch for calculating thermal stzesses (NB-3545.2(c) -1), in. tm minimum.body wall thickness as determined by NB-'3541, in. Te maximum effective metal thickness in crotch region for calculati'ng thermal stresses, (NB.-3545. 2 (c) -1), in.. hT2 hlaximum magnitude of the difference'n average wall temperatures for walls of thicknesses te, Te, resulting from 100ol'/hr fluid temperature change rate, oF Thicl'ness of cover cap behind bolt head, in. T2 Th'ickncss of shaft behind spring pin, in. T3 Thrust collar thicknoss, in. . Cover'cap thicknos's, in. Adapter plate thickness, in. -10- P < ANAlSS1 S NAif)!NCI,ATUllfi T6 Thicl:ness of bottom bonnet plate, in. T7 Thicl'ness of top bonnet plate, lS rcquircd operating torquei.n.'hfaxiii Ug Shaft bearing coefficient of friction 'I U4 Bearing f> iction torque duc to prcssure loading (shaft j ournal.bearings) Ug, Bearing fliction torque clue to prcssure loading plus seismic load ing (shaft jo!!mal bearings) U6 Thrust bcari ng friction, torque Distances to bolts in bolt pattern 'on adap'ter plate, in. V2 .Di s tanccs to bolts in bolt pattern on adapter plate, in. DistJnccs to bolts in bo'lt pattern on adapter plate, in. '. .V4 Distances to bolts in holt pattern on adap'ter plate,. in. . V~ - Distance .to bolts in bolt pattern on bonnet, in, V6 . Distance to bolts in bolt patte)n on bonnet, in. V7 Distance. to bolts in bo.lt pattern on b'onnct, in. V8 Distance to bo1ts in .balt pattes;n on bonnet', in. ~ Tota1 bolt lo~d, pounds Va1 vc Me i!!h t, pound s b2 'all jo hci <<1>t',pounds Opc!'»tor 4'c31 . N4 plato assembly'3on»ct'nd:«1»pter ! eight, 'pounds 1'I .".'i'zc 6 Weld 0 1'i sc st rue tul'a) !!olds, in. ANALYSIS NOMENCLATURE r Zl Bending section modulus of bonnet welds along x-axis, in.> Z2 Bending section modulus of bonnet welds along ~ y-axis, in.> .Z3 Torsional section modulus of'ottom bonnet welds, I.ne 3 Torsional section modulus 'of in.3 top bonnet welds, Z7 Distance to edge of disc hub, inches 4y static deflection of component,'aximum inches U3 Shaft bearing coefficient of friction U4 friction torque due to pressure'earing loading (shaft journal bearings) Ug Bearing friction torque due to pressure loading ( plus seismic loading (shaft journal'bearings) Thrust bearing friction torque -12- At~ALYSIS Nll, 1L'iNCLATVlhE S (1) Combined bending stres.'n dis.c", ps i S(~) Bending stress in disc due to bonding along the" shaf t, psi 'I S(~) Bending stress in disc ~'ue to .bending about the shaft, psi $ (l) Shear tear out of shaft through disc, psi S(S) Combined stress i'haft, psi ~ S (6) Combined'bending stress in shaft, psi . S(7') Combined shear stress in shaft, psi S ('8) Bending stress in shaft due to .seismic and pressure loafs along x axis, psi S(9) Ben'ding stre'ss. in shaft due''o seismic load along y axis, .psi S(103 Torsional shear st,ress in shaft due to operating loads, psi unreduced S (11) ~ Direct shear stress .in shaft due to pressure and seismic loads, psi S(12) Torsional shear stress't pin cross- section, psi S (13) Combined shear. stress in pin, psi I S (14) 'ircc't shear stress in pin due to seismic load, ps'hear S (15) stress in pin. due'o torsional load, ps 1 S(16) Bearing stress on pin, psi S(17) Compressive stress on sh;lft bearing'due to seismic and pressure 3.oads, psi S (1 s) Shear tear out ol: cover cap bolt through tapped hole in bo t tolll trunnion ~ ~ S (19) Sheai tear 'out of cover .ap bolt through cove'r ca'p, psl. I 19 ANALYSIS NO" I'.NCl.ATURL'(20) Combined stress 'in cover cap bolts, psi S(21) Shear stress. in cover ca~: bolts due to torsional 'loading, psi S(22) Direct tensil'e stress in cover. cap bolts due to seismic and pressure Ioa . S(28) Shear load on thrust collar spring pin, pounds S(29) Bearing stress of'pring pin on thrust collar, psi S(30). Shear tear out of spring pin through thrust collar, ps1 S(31) Shear tear out oi',. spring. pin through botton> of the shaft, ps'i ANALYSTS NOi ~L'VCLATURL' S(32) Shear te:ir. out of trunnion bolt through tapped hole in trunnion, .psi S (333 l)earing stress of trunnion bolt. on tapped hole'in trunnion, psi S (.34)- Bearing stress of trunnion bolt on'..through hole in bonnet plate, psi s(3s) 'Shear tear out of trunni.on bolt head. through bonnet plate, psi 'I S (36) Combined stiess in trunnion bolt, psi S (37) Direct tensile stress in trunnion bolt, ps'i S(38) Tensile stress in trunnion bolt due to bending psi 'oment, S(39) Direct shear stress in trunnion bolt, psi S(40) . Shear stress in trunnion bolt'ue to tors.ional load, psl Shear tear out .of operator b'olt head through hole in bonnet, psi . s(42) Bearing .stress of operator bolt on thr'ough hole in bonnet, .psi 'S (43) Combined stress in operator bol'ts, psi s (44) Direct. tensile stress iv. oper'ator bolts, psi s(4s). Tensile stress in operator bolts due to bcndi'ng moment, psi s(46) . Direct shear stress in operator bolts, psi 19 AfJAL'YSIS NO!!L'HCLATVRE ( s(47) Shoar stress in operator bolts due to torsional loads; psi S(4s) Combined .stross in bonn..t body, psi 'S (4g) Di'rect tensile stress i»-bonnot body, psi S(50) To»sile stress ii> bonnet. body .due to'bending moment, I PS1 4 S(Sl) Direct shear stress in bonnet body, psi ' .S(S2) Shea'r stress in bonnet body due to torsional load, PS1 s(sg Combined, shear stress in bottom bonnet iield, psi S( 54) Total'tensile stress i'n bottom bonnet weld, psi '. S(55) Direct ton'sile st'ress in bottom bonnet weld;. ps' S(56) Tensile stress'n bottom bonnet weld'due .to bending moment; psi , S(57) Total shear. stress in bottom bonnet weld., psi s(hs) Direct shear stress in bottom bonnet weld, psi S(59) Shear stress in bottom bonnet weld due to torsional load, r r psi S(60) Combined .shear stress in -'top bonnet weld, psi t S (61) Total tensi'le stres's in top bonnet weld; Ps.i S( 6.2) Diroct tensile stress i:n top bonnet weld, psi S.(6S) Tensile'tress in top bonnet weld. due to bending moment, psi S(64) Total shear stross in top bonnet weld, psi S( 65) Diroct shoar stross in top bonhot wold, psi S( 66) Shear stress in top bon»ot weld .duo to torsional load, psi 0 ANAL'YSIS Nol!O'NCLATURE S(67) Combined stress in trunnion body, psi S(68 ) Direct 'tensile stress in trunnion body, psi S(69) stress in. trunnion body due to bending moment, ps1 ps'ensile S(70) Direct shear stress in trunniop body, psi stress trunnion body'ue to S(71) 'Shear in torsional'oad, SUMMARY TABLL',I NTRODUCT ION In the following pages, the pertinent data for the butter- valve stress anal>sis fly .is-tabulated. in three categories.'. Stress Levels for Valve Components- 2. Natural Frequencies of Components 3.'alve Dimcnsiona1'ata In Table 1, Stress Levels for Valve Components, the following data is tabulated: Component Name P Code Reference (when applicable) Stress Level Name and Symbol, C 'Analysis Reference Page hfateri'al Specification'ctual Stress Level Allo'wablc Sti css Level The niaterial specifications are taken from Section II of the 1 . code when applicable. 'llowable stress levels are Sm .for . . tensile stresses and .6 Sm for shear str'esses. The allowable 4 codex'n levels're the same whether the calculated, stress is a combined stress or results from a single, load condition. Sm is the'esign stress intensity value as dciincd in Appendix I,'ables 1.-7 ' of Section III of .the Table 2, Natural l:rcquenci cs of Valve Componen'ts,. thc. following d'lta is t Lbulated: za Summnr, Tab1e Intro~luct ion :Componen t Name Natural Frequency Symbol Analysis Reference Page Component Materi al: Natural Frequency In Table 3, Valve Dimensional Data, the values for 'the pertinent.yalve dimensions and parameters are given. TABLE 1 STRESS LEVELS FOR LVE'COMPONENTS ALLOHABLE CODE REF REF STREGS STRESS LEVEL COMPONENT PARAGRAPH SYMBOL & NAME PAGE MATERIAL LEVELS PSX 'SI Body NB-3545 ' Primary membrane Sm stress in crotch 35 ASME SA«516 GR S5 13700 . Primary membrane PI ASME SA-S16 GR;55 Sm. stress in body m 13700 NB-3S45 ~ 2 Primary plus ASME SA-516 GR 55 secondary stress due WSe o to internal pressure 13700 B-3545 ' Pipe Reac'tion ASME SA-516 GRe55 1.5 Sm stresses 20550 Axial Load Ped 36 9 &5'5 Bending Load Peb 36 4.1 ec Torsional Load Pet 36 S'm 4. I 0 0 8-3545 ' Thermal Secondary ASME SA-516 Gr.55 llc Sm stress 38 13700 B-3545 ' Primary plus S ASME SA-516 Gr,55 3Sm secondary stress 41100 B-3545,3 Normal duty fatigue S ASME SA 516 Gr ~ 55 Sm stress Na > 2000 38 13700 Disc B-3546 ' ombined bending S {1)'9 ASME SA-516 Gr.55 1.5 Sm stress in disc 20550 B-3546 ' hear tear out of S|4)'1 ASME SA-516 Gr.55 ;68m haft thru disc 9>b 8220 ~ ' ~ ' ~ ~ ~ ~ ~ ~ ~ ~ ~ e ~ ~ ~ ~ ~ e I ~ ~ e ~ ~ I ~ ~ ~ ~ ~ ~ ~ ~ e I ~ e e I e ~ ~ ~ ~ C ' I ee I ~ e ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ 0 ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ o e I ~ ~ ~ I ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ 1 ~ ~ ~ 0 ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ ~ 1.9 c TABLE 1 STRESS LEVELS FOR VALVE'COMPONENTS ~ ~ ALL CODE 001ABLE REFT REF. STRESS STRESS COMPONENT PARAGRAPH LEVEL SYMBOL & NAME PAGE MATERXAL LEVELS PSX PSX Operator Combined shear stres. S(53) 9.5':5 .6Sm Mounting in- bottom bonnet 7200 Contend welds Combined shear gtres S(60) 57 . 6Sm in top bonnet welds .581 7200 Combined stress 'in S (67) 58 ASME SA-516 Sm trunnion body Gr.55 13700 ~ ~ Table 2 NATURAL FREQUENCIES OF VALVE COMPONENTS Natural Natural . Component Frequency Re f. Frequency Name Symbol Page 'Material (Hertz) Body Nl ASME SA~516 Gr. 55'BSx Banjo FN2 60 ASME SA»564 87&6 Type 630 Cond. H~1150 Cover Cap 60 ASME SA-516 N3 Gr.70. 'Bonnet N4 61 SME SA-36 ~ ~ Job Number: Valve Siz,e: Operator Mounting: Operator: .. Cp C6 Gb 'y Gg Ag -1 ~ o cs ~ AS Cg .gx A6 .gy, Ay As Dl H2 ~ 'By c .B2 Dg ~ ~ c BB D4 HS . ",l H6 BS '- ~ ~ D6 Hy Dy tc Hs. By 'g,' Bs, ~ ~ I'2 C Pb J ~ Cb Ia Cp IS * Co I6 ~ c, Iy -2G« 19 hT2 Mx T2 l Jg'4 Mx lo.. w Js My T4 MS Ko K1 N1 T7 TS U1 ~ i '.K4 Pd U2 pr >s V1 ( . V2 L2 ). o. Vg V4 1 ~ 0 V5 R4 V6 Rs V7. L7 VS LS R6 ~ e Lg l.o .~ Te Wg 26a N~ X Y ~O. zz P 27 I 261) Standard, Stress Report for NRS Butterf'ly .Valve'ith Bonnet hfounted 'Cylinder Operator -27- 19 ANAIYSIS INTRO)mCT ION 1 . Described in t)!e following pages is tho analysis used in ver'defying thc structural adequacy of the main .elements 'of the N) the analysis, the .design rules for Class 1 valves are used, . since the .rcquiremc!its for this .class of valve is much more explicit th!!n for. either Class 2 or 3 design rules. -The de- sign rules for Class 2 and..3 arp exceeded by the rules for Class 1 valves. Valve components a'e anal>'zcd under thc assumpti'on that 'he valve's either at maximum fluid dynamic torque or j;. seating against the maximum design prcssure. Analysis temperatUre is 'I 300o)'. Seismic accelerations are simultaneously applied .in each of three mutually perpendicular directions. Seis'mic loa'ds are made an 'integral part of the analysis by the inclusi:on of the «cceleration constants gx, gy gz. .The symbols gx, gy, gz represent accelerations in'he x, y and z directions rcspectivcly. These 'directions are defined with \* respect to thc valve body centered co-ordinate system as illus- tratod in )'igi!rc 1. Specifically, the x axis's along thc pipe axis,, the z !xis is:!long thc sh:!ft axis, ai>d the y a'xis is. mutually pc! pondicul!r to'thc x gnd -z axes, formii>g a right hand tri.ad wi th them. j e 'i : ~ 'e'~a r R~t r ~~f r' r r're Zp/ i' zr„Yr +Y i ''f.euro 1 yn( y~'' ~~n~»'~"~1'1Aj, ou>j:.v> u'l,oN -29- \ ~ 19 Anal sis Introduction 'Valve orientation with respect to gravity is taken into'ccount by adding the appropriate quan'tity .to the 'seismic loads. The justification for doing this is that a gravi- tational load i.s 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 appropri:ately titled section. In addition to containing sketches where appropri.'ate, each section coritains an explanation .of 'the basis for each calculation.'here. applicable; it also contains an A „interpretation of code requirements as they ap'ply .to the analysis. ' . Figure 2 is a cross-.section view Of the butterfly valve,'nd its associated compo»ents. Dotailed sketches are provided throughout the report'o,clearly define the geometry. Disc Anal sis Shear Tear Out of Shaft The-disc is designed so the minimum thickness of material surround- ing the shaft extension in the disc is above the shaft on the arch side. The loading is due to both seismic and pressure loads. mP R +N + +g 4. 2 gx z s P = Shear tear out shaft . 2J, (K2+D (1-SZN 4S )) through disc, psi. 0 ~ ~ ~ SIIAFT ANALYSIS The shaft is analyzed in accordance with Paragraph NB- . 3S46.3 of Section I!I of the Code.. The shaft. loading is a com- bination of seismic, prcssure and operating loads. Maximum torsional loading is either a combination of seating'nd boaring torque or bearing and dynamic torque. Columnar stress is not considered in the shaft. loading due to its'. negligible effect 4 on the stress levels. F'igure '2 shows. the banjo .assembly with. the ~ ~ through shaft. S'haft stresses due to pressure, seismi:c and operating loads: S (5) = S (6) + (S (6) 2+4 S (7) 2) Z where S.(6) = .(S(8)'S.(9) )~ = Combined bending stress, psi S'(S) = (11R42Ps+N2gx) . 23 B1RS = Bending tensile stress ''25 due to pressure and seismic RS loads:along x axis," psi. S(9) = . 25li'gg .'yRg = Bonding tensile stress due . 25 > I~kg to seismic loads along y aMis, psi . S (7) = (S (10) 2+S (11) ~) < Combined sh'oar stress, psi S(10) = TBRS Torsional shear stress, psi ~S>< Rg S (11) = 1. 333 SmR42I's+'N2(g 2+g 2) = Direct sl1car stress, psi MRS Also worthy. of ittcntio11 is, tho torsional sl1ear stress't thc rccluccd cl'oss -sect1'oil whcl c tho pin passes through the shaft. 42 ~ ~ PACKING SIIAFT BEARINGS- SEAT ' DISC DISC PIN BEARING Sl!AFT gl "L COVER CAP ~ .pQ ~@~~~~ COV!:R CAP.!3O!.TS. FIGURE 2 ViiaVE CROSS-SECTION 31 END CONMI!CTION ANALYSIS The NRS butterfly valve is a uniflange desi.gn. Rather ~ than having,flangcs that are external to and distinct from ~ the body, tl>c body shell is fabricated so that the end ' connections are machined directly into the body shell. The ~, I outside and inside diameter of the body .shell conform to the requircinents. of,the American National Standards Institute (ANSI) standard B16.5.. The end connections, either flanged 'or ti'eld end, also, conform to this standard., ' -32- BODY ANALYSIS The body analysi's consists of calculations as detailed in'aragraph NB-3540 of Section III of the'ode. Paragraph NB-3540 i.s not.'highly oriented to valves as butterflyf related to v'arious 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, it is explained in„.the subsection containing that . calculation description. Figure 3 illustrates the essential features of the .,body geometry through the trunnion area o'f the valve'. he symbols used to define specific dimensions are consistent wi;th. ..those used in the analy'sis and with the nomenclature used 'il. the Code. 1. Minimum Bod Wall Thickness ~ Paragraph NB-3542 gives minimum body wall thickness re- quirements for standard pressure rated valves. The actual minimum wall thickness in the NRS valve occurs betwe'en the flange bolt holes and body bore. «3 3 « Pal'.SSUPiE -Al 110DY C) "I'inure 3 34 Bod Analysis .2„ Bod Shh e Rules The NRS valve meets the req'uiremcnts. of Paragraph 'NB-3544 af the. code for body shape rules'. The ex- terna] at fillet trunnion to,body intersection must'c greater than thirty percent of the minimum body wall thickness. 3. Primar Membrane Stress Du to Internal Pressure . Paragraph NB-3545.1 'defines the maximum allowable str'ess in the nech to flow'assage junction. In a. 'I butterfly valve, this corresponds with the trunnion to body. shell junction. Figure 3 shows the geometry thr ough this section. I The code defines the stresses in 'thi:s area using the pressure area method. As seen in Figure 3, certain 1 code-defined dimonsi.ons 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 flow .pattern, as the nock extends .to the face of the body. To,comply with the intent of the code, the areas Af and Am are interpreted as shown in the cross- section (Figurc 3).. Using those areas, the primary ' membrane stress is thon calculated. "m = (Ar/Am'" 5') ps -35- Bod Ana3 sis k As an alternate method of determining the 'primary membrane .s t res s, an equiva lent analysis f'r primary membrane stress is applied to an area'way.from the trunnions.. In these areas, the metal. area and fluid 'rea are as. shown in Figure 4.: Since'he depth of 'he metal area is equal to the depth of the fluid area, the ratio Af/Am is equivalent. to the mea'n radius of the,body over the thickness of t'e body shell; Rm/Hg; The primary membrane stress t1>rough this section's .then: ~ ~ r Pm' (Rm/»9+ 5) ps 4'; Secondary Stresses A. Body Primary plus secondary stress due to 'internal e pressure.'aragraph. NB.-3'S45. 2 (a) of Section III „- . of the code defines the formulas used in calculating this stress. ri + .'5 '.. Secondary stress due to pipe reactio'n: . Pa'ragraph NB-3545.2(b) gives the formulas for finding stress ,duo to pipe reaction. Pod = 'FdS (1)ircdt'or Axial Load 'Effect) 'd = I'eb Cbl'l>S'ib (Bv.'nding Load Effect) Pet = 2FbS (Torsional Load 'Effect) Gt -36- ~ Ag Rm 'RES SURE ARI'A AHALYSIS CROSS-SECTION IN BODY figure 4 Bod Anal si s C C. Thermal secondary stress: Paragraph NB-354'5.2(cf of Section III of th'e code gives formulas. for determining the thermal secondary stress'es in the pipe. QT =: QTZ + QT2 Nhere CGC2hT2 D. Primary plus secondary stresses: This calculation I is'per Paragraph NB-3545.2 and is simply the sum of the three previous secondary stresses. = Sn Qp 'e 'Qt 2 'Sm 5. Valve Fati uc .Re uircments I Paragraph NB-3543. 3 of Section III of the code .defines requirements for normal duty valve fatigue'.'. The alloiiable stress level is found from Figure I-9.0. Since the number of cycles is unknoMn, a maximum I value of. 2,000 is assumed. The allowable stress can then be found from Figurc I-9.l for carbon steel. This then gives an allowable stress .of 65,000 psi. = ' Spl '/3 Qp Peb/2 + QT3 +' ~ 3QTl p2= Qp'b'll'c rc: QT3 = CoC3~T2 e DISC ANAJ,YSIS Sect'ion Nl>-354G. 2 defines the'esign requirements of the valve disc. Both'primary bending and primary membrane stress are mentioned in this'ection. For a flat plate such. as the 'I I .butterfly valve di'sc, metnbrane stress is not defined until the deflection.of the .dirac reach'es one-half the disc thickne'ss. 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 NRS butterfly valves. Thc disc is designed to provide a. structurally sound pressure retaining component ~elhi,le providing the least interference to the f lofti'. 'I Priear 'Bendin Str'ass Due to the manner in'which. the disc is supporte'd, the disc experiences bending both along .the shaft axis and about the shaft axis. The combined bending stress is maximized'at the disc center Whore the maximuii> moment occurs. The moment is -a result of a uniform pressure load. Combined bending 'stress in disc: S(1) = (S(2) + S(>) ) re: ''hc = S(2) ~ 90433 I'sR4 C7 Bending stress duo to moment .along shaft axis, psi I4 ~ ~ S(~) = .GGGG. l,.l<,,'C, Bonding stress duo to moment I3 about shaft axis, psi -39- S1IAFT ANALYSES The shaft is analyzed in accordance with Paragraph NH- . 6.3 of Section EEE of the Code., The shaft. loading is a com- ation of seismic, pressure and operating loads. Maximum sional loading is either a combination of seating and boaring .que or bearing and dynamic torque. Columnar stress is not siderod in the shaft loading due to its', negligible effect the stress levels. Figure '2 shows. the banjo .assembly with the rough shaft. Shaft stresses due to pressure, seismi'c and operating loads: S(S) = S(6) ~ (S(6)2.4 S(7)2)~ 2 where S(5) = (S{8)-+S(9) )< = Combined bending stress, psi S'(8) = (~R42Ps+l" 2gx) . 2S 81RS = Bending tensile stress .'25 due to pressure and seismic RS loads along x axis, psi. S(9) = .25II29, B2R5 = Bonding tensile stress due . 25 m I~IS to seismic loads along y aMis, psi', S (7) = (S (10) 2+S (11) 2) 4 Combined sh'oar stress, p'si S(10) = TBR5 Torsional shear stress, psi S~iR " = = S (11) 1 ~ 333 S T(R< 2P s+ . SN2 (gx2+ 2) Direct shear g stress, psi Iso worthy. of attcntiop is. thc torsion'al sliear stress at thc educed cross-section whcrc tho pin passes through the shaft. 42 19 Shaft An;ilysis S(12) = S(10) "Rg " - D)D) - D)Dp ~1 '1 43 ~ e A DISC Pl 'NALYSIS's seen in Figure 2, chere is one through shaft and one disc pin. The pin is subject to seismic and torsional loads. Combined shear stress in top disc pin'. S(13) =, (S(14) 2+S(15) 2)" P Direct, stress on disc pin due .to seismic loads: .S(14) - W7g, ?Nl('785) D32. Torsional shear stress in disc pin: I ZNlR5.785D3 stress on disc. pin:'earing S (16) T8-.5U5 2R5K293N1 Where: U4. = . 785 (2R4) PPU3R5 = "5 "4+'~2gx"3 5 0 PO ~ Actual Shut-Off Pressure 44 Sl tAFT BEARIKG ANALYSIS The sleeve hearings in the trunnion ( Figure 2) are sub- jected to both s'c i smic and pressure loads. = S S(1? ) 'PdR42+l(2 (gv2+Pv2) Compressive streSs on 2. 1.5l)2 shaft bearing, psi ' COVER CAP ANALYSIS ~ - ~ ~ I7 6 shows the bottom trunnion assembly, including the cover 'igure cap and cover cap bolts. 1. 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 tensile loading equa11y. "Shear tear out of bolts through tapped holes in trunnion: : + %418) . W2 gx g gz Ps 'R6 ' J3 2.83 D6 ::-:%hear tear out 'of bolt heads through cover cap, psi: — Q(19) W g 2+g "Z~g 2 + ~ 62 .=W T1 S.2 D6 ~Combined stress in bolts, psi: (20) = S(22) + ('(22) + 4S(21) ) 2 .2 -.='..-Where: ..$,(21) ~ .25 N2 g +g ~+g 2 (D2 + .66 t.'D4-D2)) '707 H~ 4 A4 ~ .Shear Stress in Bolts Due to Torsional Load. BOTTOM TRUNNION 'SHAFT BEARING BOTTOhj SHAFT THRUST COLLAR PRING jtagrag@ ~ PIiX'OVER CAP COVER CAP BOLTS SHINS BOTTOM TRUNNION AND,THRUST BEARING ASSEMBLY Figure 6' Cover Ca Anal sis $ (22) ~ +gy +gz + > Ps R62 N2 g~ = Tensile Stress in Bo1ts 4 Due to Seismic And, A3 Pressure Loads, psi 2.. Cover cap stresses: The combined stress in .the covercap is calculated using the follow- ing formulas: S(23) = S(24} + S(25} + -((S('24} + S(25}) + 4S(26) ) -2 2 Nhere: S'(24) ~ 3(.785 (D4 + .25) Ps + N2gz) Radial Stress ~ 4z T4 ~ : S(25) 3 ( 785 (D4 + ~ 25) Ps + NZgz) (. ~ Tangential Stress 4 ~ vT4m S(26) = .785 (D4 + .25) Ps + N2gz Shear Stress ~ (D4 + .25) T4 48 THRUST BEARING ANALYSTS 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 position- ed to maintain optimu'm sealing. Formulas used to analyze the assembly are given below. ..1.. Bearing stress on thrust collar due to seismic and pressure loads: 2 2 8(27) ~ W2 2+g 2+g + „ P R 78S (D42 D2+ '5) 2) ~ ~ .2. Shear-load on thrust collar spring pin due to seismic, pres- re 'and torsional 1oads: t ';N(28) (WZgz+ m Ps R5 ) + . 25 WZgz (DZ+. 0833+. 66 (D4-DZ) ) RS Bearing stress of spring pin on thrust collar: 2 (29) ((WZgz+'Ps RS ) + (. ZS WZgz) DS (D4 -DZ) - 4. Shear tear out of spring pin through bottom of shaft: :.'S(31) WZg + «,Ps RS ~ ...2DZ TZ ,,e 49 , OPERATOR MOUNTING ANALYSIS The operator mounting consists of the top trunnion, the bonnet, 4 the operator housing, and the holt connections. The elements of H the assembly are shown in. Figure 7. l. 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. 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 of trunnion bolt through tapped hole in top trunnion. 2[22) =I'*ll g +g *g g(J ~ H) 2 {J 2) 4 .: HJJ *2(J)+Hg). 22 ~ 2(J H )2 .9~ L4D7 (b) Bearing stress on tapped holes in trunnion. S(33) = M + T (F +F ) ' N (g +g ) z 8 + x y x y 4(.707 H2) 4 4 D7L4 (c) Bearing stress on through hole in bonnet. S(34) ~ M + T8 (F +F )~ N (g +g " ~ 4(.707 Hp) 4 '4 D7T6 50 TOP TRUNNION MOUNTING FIGURE 7 4 FILLET. 4'ELD ALL AROUND ~ ~ ~ '» i .' ' .»I . . ,{ 'fI>( ~ . » I ~ ~ BONNET TOP TRUNNION \ YALVH BODr TRUNNION BOLTS ~ ~ 19 Operator Mounting Analysis d. Shear tear out of trunnion bolt heads through .I bonnet, S(35) Fz+N4gz + Mx(J2+HZ) + M (Jl+H2) 4 'JZ +2(J2+H2) 2 2Jl +2(Jl+II2) 5.2 D7T6 e..Combined stress in trunnion bolts (See Fig; 8) = > S(36) S(37)+S(38) + ((S(37)+S(38) +4'(S(39)+S(40) ) 2) 2 . 2 Where i S(37) = Fz+N4gz Direct Tensile Stress, psi '4 A5 = S(38) Mx(J2 F12) + M ( 1H2) 2 2 due extended 2J22 2 (J2+II2) 2 J12 2 (Jl+H2) to 1 1 2 mass bending '', c: . ~ '5 . moment, psi ~ ' 'S(39) 2, 2 2 Y 4 x . Direct shear .4 A6 stress, psi = - = S(40) (Mz+T8) . '- Shear stress due to . torsional load, psi ( 707 FI )4 A Shear tear out of operator bolt. head through hole in' bonnet. = S(41) Fz + "x(J4+FI4) + M (J3+I.I4) NZ 2J4 +2 (J4+H4) 2J3 +2 (J3+FI4) ~ 5.2 D8T7 g. Bearing stress on tapped holes in bonnet. '))i ) = )) ) ()'„)+) )) ).7) Iii) ')D8T7 (0 Kg Jy ' TOP TRUiXAIO.l BOLTIXG Figure S 0 erator Mounting Anal sis A h. Combined stress in operator bolts (See Fig. 9) S(43) S(44)iS(45) + ((S(44)'+S(45) ) +4 (S(46)+S(47) ) 2) 2- 2 Nh'ere. Fz ',= Direct !'(44).='tensile stress, psi'ZA7 ' '! 'S(45) = Mz(J4+H4) + My(J3+H4) = Tensile. stress due to bending, ZJ42+2(J4'+H4)2, ZJ32+2(J3+H4)2 psi A7' ~ !!6! = jj„"!!)! = D' NZA8 s(47) = M,+T8 = Shear stre'ss due to'orsion, psi (.707H4)NZA8 2. Bonnet Stresses .The bonnet stresses are calculated with the assumption that loading is through the bolt connections as previously defined. a. The maximum. combined stress in the bonnet was calculated using the following formulas: S(48) = S(49)+S(50) + ( S(49)+S(50)) 2+4(S(51)+S(52)) 2 = Combined stress in bonnet legs S(49) + Fz+N4gz = Direct tensile stress, psi B5 P H4 '4 'g BONNET BOLT PATTERN II F.igurc 9 55 0 erator Mountin Anal sis S(50) = Mngg + M B0 = Tensile stress due to bending moment, psi Where s S(51) = (F +F ) + N4(g +g ) = Direct shear stress, B Psi 5 S(52) = T Cp = Shear stress in bonnet body due to Kp torsional load, psi Where T = Torque, in-lbs. 'Cp . Torsional constant for non-circular cross section Kp = Function of cross-section, in. b. The maximum combined, shear stress in the bonnet mounting plate to body welds was calculated using the following formulas: Bottom Bonnet Weld 2 S (53) = S(54) 2+ 4S (55 = Combined shear stress in 2.'ottom weld, psi Where S (54) S(56) + S(57) = Total tensile stress, psi 'I S (56) Fz+W4gz Direct tensile stress, psi.. 1 S(57) Mx + ~ = Bending tensile stress S(SS) S(58) + S(59) = Total shear stress S(58) (Fx2+F 2)< + W4(g„2+g 2)< = Direct shear stress, ps l. v 56 erator Mountin Anal sis S(59) Mz+T6 = Torsional shear stress, psi Z$ 'Top Bonnet Meld S(60) = .(S(61) +4S.(62) )~ = Combined shear stress in top b'onnet weld ~ ~ a'here S(61) S(6 3)+S(64) = Total tensile stress, psi S(63) Fz Direct tensile stress, psi U2 S(64) ~ Mx ~ M ~ + ~ = Bending tensile stress, psi 1 2. ). 'S(62) = S(65)+S(66) = Total'shear stress, psi = . S[65) ')F„+P )" D', )* ~ ~ S(66) = Mz+Ts = Torsional shear stress, psi'4 c.. Trunnion Body Stress The trunnion body stresses are'alculated using the fallowing assumptions: l. Operator loading is through the bolt connections. 2. There is an equal, and opposite reaction to the bolt loads at the body. ~ ~ ~ t 0 erator. Mountin Anal sis The combined stress in'the trunnion body was calculated using the following formulas: ~ S(67) = S(68')+S(69) + f(S(68)+S(69) ) +4(S(70)+S(71)) )~ ' 2 2 .Where = ' .S(68) Fz+N4gz . Direct tensile stress,, psi I K4KS .. 785B22 .S (69) = (Mx+F K6) 5K4 + (M +F K6),5K5 .= Bending tensile st'ress, psi .0833KgK4 -mBp 33K4K53-mB24 64 64 C S(70) = .(F +F ) ~+N (g ig )~ = Direct shear stress, K4K5-.785B22 psi'"Torsi'onal S(71) = (Mz+T8) .5(K4 +K5 )+ shear stress, A psi .0833(K4K53+K5X4 ) -mBp4 32, Fl A. Introduction To calculate the, natural frequoncy. of'he various components of the NPS valve, a model system with a single e degree of frccdom is constructed. The individual com- ponents ai>d'roups of components are modeled and analyzed as restoring spring forces which act to oppose th'e re- spective we'ight forces they are subjected to. The static e deflection of the. component is calculated and is related to natural frequency" as: Fn = 1 K or Fn '2n Li y or Fn = o'. s "- Ay t ~ The analysi.s details the equations and assumptions used in determining the natural frequencios listed 'in the suminary table. Sl-etches are provided where appropriate. B. Valve Bod Assembl " Tlie body shell, as seen in Figure 1, is assumed to cxpcri.cncc loading duo to the cntirc valve weight. Not:ural Frequency of'ho body shell: l~ FN1 = Ay~ 59 Fre ucnc Anal. sis ')'here Ayl = h'll.13 = Maximum deflection of body shell due to .valve weight, in. 48 L'5 C. ~Di A. I 1 Figure 2 sho«s the banjo assembl'y in the body. The. natural frequency of the banjo assembly. is calculated using thc fol'lowing:1 1~ FNZ 9.8 Ay2 Where ~y2 = N781 3 ='aximum deflection of shaft, inches 12 L 16 D. Cover .Ca Assc'mbl I jO As. scen in Figure 6, the cover cap supports the .banjo. The natura.l frequency of the cover cap is calculated as follows: FN3 = Nhere 3(m2-1) 4'2 (. SD4+.125) = Maximum dcfloction of cover cap 16mL'1'4 m, B. Bo»»ot Asse~»>l>1 Figure 7 shows the top trunnion assembly. The following assumptions arc made in calculating thc bonnot cnatural frequency: 60 Frc< ucnc Anal sis / 1. The worst valve assembly mounting position is where the bending moment, is predominant 'in producing de- flcctio».* ~ 2. The bonnet is .assumed'ixed at thc top trunnion. 3. 'Thc adaptc'r plate is assumed to be. integral with and have a cross-section the same as the component it mounts to. Natural frequency of, bonnet: 9.8 ~V4 4'here = ~ hy4 1);1$ g +N4k3~ + NgZoHS 3BIy ~hip / j' 4 ~ ~ j ! . PARTS AND MATERIALS OF CONSTRUCTION PARTS AND IIATERIALS OF ICONSTRUCTION ., ( I. BODY: NAT'L.e SA-516 GR. 5 "2 12. GREASE: DOW CORNING I II 2. SEATING SURFACE: MAT'L.e SA-479 TYPE 304 I3. 0-RING:, NAT'L.e E.P.T. I DISC: MAT'L.e SA-%le GR. 5 2 l4. BOTTON COVER: NAT'L.e SA-5lb GR.70 4. SEAT: MAT'L.e E.P.T. l~. COVER BOLTS: MATrLi .'A-l93 GR. B-7 MAT'L.e CARBON 5. CLANP SEGMENT RING: MAT'L.e SA-282 GR. C Ie. LOCKWASHER: STEEL 6. CLAMP SEGMENT SCREWS: MAT'L.l SA-l93 GR. 8-7 l7. BOTTOM BEARING: MAT'L.e ASTM B&38 GR. I TYPE 2 BRZ. 7. SHAFT: MAT'L.~ SA-e264 TYPE 630 COND. Hl ISO IB. TOP BEARINGS: MAT'L» ASTM B-438 GR.I TYPE 2 BRZ. MAT'L.'e +I 8. PINS: MAT'Le SA-320 GR. BBM l9. SHAFT SEAL: E.P. T. 20. PACKING RETAINER RING: MAT'L.; SB-l44 ALLOY 38 9. THRUST COLLAR SHIMS: MAT'L e HARD BRASS PACKING: MATrLe E.PT. V-RINGS IO. THRUST COLLAR: MAT'L.; SAE 660 BRONZE 2l. 'AT'L I I. THRUST COLLAR PIN: NAT'L.e AISI 420 STN. STL. 22 LANTERN GLAND RING y ASTM A 269 1 VP 'I I I 7'TUB SHAFT COATED WITH SILICONE'UBRICANT.'OR II ASSEMBLY PURPOSES ONLY. . I I (' s NOTE: I-PIN THRU CENTER OF 8 DISC FOR 6" AND 8" VALVE. I-PIN TOPe AND I-PIN BOTTOM FOR IO('ND l2" VALVES. IO I'7 l9;, I I4 22 . l/2" NPT FCR LANTEIs!I CLAINC BLEED-CFF . ( CIAP PE O WiP I PE PL CC t IN VALVE BC"T. le I2 ,, I I I I 8 20 2l 6 I/2" liPT BLEED-OFF I t.' C C!i C T I Ot 1 STUB SHAFT COATED WITH (cAPPED w/PIPE PLcc> BODY SEATING SURFACE SEAL WELD wlLLI,t;.. P'rr 0 . SII Tr ONE I UBRTCANT FOR BE "PT" EXANINED': .: ASSEMBLY PURPOSES ONLY. ,.-'; 'AP EBT UR,E I ;; ':j:;:,'ARD,' -MATERIAL AND NDE STANDARDS SHA W H AS CTION III CLAS 2'EQUIREMENTS. O Itt BECHTEL PowER CORP.- O w Cr CUSTOMER: tt s s I PM58-P-31 "Ac I CO P, It g I CUSTOMER O., 0 I e=,'i!: z W2 L/I PRATT ORDER NO,: o-oo26-3 Q I/I+ D o r z PENNSYLVANIA POWER B LIGHT CO., SUSQUEHANNA 'Ai O Z PROJECT: O ' j ( Gl Z— ITEH NO~ ' g mill ~, mz,— ' I Vl UNIT"I 6'!-HBB-BR-AO"5721 .xm~MD 1.17 I ' *, 4-! Dg Z '1118 UNIT-2 6"-HBB-BF-A0-5721,, . I ', I, ~ I I m o rmr mm ,I I Z I/I „'n. I ~ nVl 4~ b ? .b ' TTl I X)m o 0 ~ +,, I 's ) I z C/I ol K O I/1-1 .i4 a I ~M b 0 rarn b I/I '.X I mg EI m>2.0 I I + 4 ~ » e- ~~ VALVi= e.:.. > w(/f 'r. npcft>: JC, pftvAe, pt- I rtn ftfN err 'TIARA j G AA cC 1 512E -Im~O O -. EltfIATETA h TArr DPERA'Tftfct IriEDIA'.EAIIABoff ~ Cn fry g9r ~+Omm~ FA!LURE, SPRIIAG TG '3/g, 9 Z/z p MODE: CLOSE'(, c c ~XXIV ggP 31h TTI I.DA 7c KZ t WA Z gf mz Q (b ITI N O Z IO > Z. Z'TI C N go~~o I r l2 o o ki . Ill ! CAI Of Qo +z gO 0 NQ- s -. Z ~ ', 4 t. 0 iX Qo +Y.. :-"- poslrloN I ''.,:..-.="",poslrloN t. -)- -; Qo Qo FLANGF x YIELD END ' Y" s-"'-/7-75 .. I Qo ' B Qo Qo i II-Zl- . r -fP-'jI; /'FV .PATE 8t APP I kf V DATE PRAT T t-0 fkA I ')! Jt q Hi NRY - ELF =NO. AND SIZE OF HOLEIS QF NERAL ARRANGE.MENT E DEE'P. STRADDLE CENTE.RL1NE': NUCLEAR H.R.S. VALVE Vl/BON 15OL8. USAS FLANGE BOLT LAYOUT. f BETTIS SPRING RET'URN OPER. NOMINALVAlVE SIZE POSITION 2 POSITIOfd — = R,F.. NOWT t. — DD DIA. ~I/'28 NP r BLEED-OPF CQMNECTIOld I ftCAI.f. 'AT G= BOLT ClRCLE (0APPED WjrPIPE, PLUG) DAAAN tITJ~Df ''jf -r ( IIEEAf D kf ~ rJ'" J P RC. APf'kO'Jf D / i ''AMT APERTURE 'I D QP g/~ I, ~ ( CAR !3 DAD.:ID t t t ~m