ML20212F265

Verification of RELAP5-FORCE Hydraulic Force Calculation Code

ML20212F265
Person / Time
Site:	Rancho Seco
Issue date:	05/30/1984
From:	Cajigas J GILBERT/COMMONWEALTH, INC. (FORMERLY GILBERT ASSOCIAT
To:
Shared Package
ML20212F255	List: ML20212F250 ML20212F265
References
NUDOCS 8703050055
Download: ML20212F265 (84)

Text

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I Verification of the RELAP5-FORCF_

g Hydraulic Force Calculation Code I

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VERIFICATI0ti 0F THE RELAP5-FORCE 8,

HYDRAULIC FORCE CALCULATION CODE BY I

J. M. CAJICAS GILBERT ASSOCIATES, INC.

P.O. 30X 1498 READING, PA 19603

!I May 1984 I

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f mi 1.0 I"TRODUCTION RELAP5-FORCE (1) is a modified version of RELAP5/ MOD 1(2) which includes a hydrodynamic forcing function calculation option. This version generates time-dependent force functions for piping segments cefined by the user.

RELAP5/ MOD 1 has been modified to selve tne hydrodynamic force equation for the requested RELAP5 volumes, at each time step, and write the resultant force to the RELAPS output print and plot files.

This report documents and verifles the accuracy and validity of the enanges to RELAP5/ MOD 1.

The verification process will include:

1) RELAPS/ MOD 1 Changes Verification. This verification will show that the RELAPS-FORCE modifications have not adversely altered the precision of i

the RELAPS/ MOD 1 calculation.

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2) Hydraulic Force Calculation Verification - EPRI/C-E PWR SRV Tests. This verification will show the adequacy and accuracy of the RELAP5-FORCE force calculation methodology by comparison to test data from the EPRI/C-E PWR SRV Test Program (3).

3) Hydrualic Force Calculation Verification - Edwards' & Hanson's Pipe Experiments. This verification will snow the adequacy and accuracy of the RELAPS-FORCE force calculation methodology by comparison to test data reported by A. R. Edards(4) adn G. H. Hanson(5). This data is particularly significant because it allows a better verification of the blowdown force option of RELAP5-FORCE than the one permitted from the EPRI/C-E FWR SRV Test configuration and data.

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ELAP *0D" CHM;0ES '?E:IF:CC:0N I

b4 The RELAP5-FORCE code was developed by progra:rcing the hydraulic force equation into the RELAP5/ MOD 1 code. This required the aedition and modification of subroutines to the program.

To show that these modifications did not alter the ::asic RELAP5/ MOD 1 calculations, a sample proolem was run for the following two cases.

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1) RELAP5-FORCE USER'S GUIDE (1) sample problem run without the force option cards using RELAP5/ MOD 1, Cycle 14 AW. RELAPS/ MOD 1, Cycle 14 AW, is the

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base code for RELAP5-FORCE, Version 14 t

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2) RELAPS-FORCE USER'S GUIDE sample problem run with the force option cards using RELAPS-FORCE, Version 14 q

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Figure 2-1 shows a schematic of the RELAff-FORCE USER'S GU,IDE sample problem. The RELAP5/ MOD 1, Cycle 14 AW and RELAPS-FORCE, Version 14 input listings are shown in Appendix B.

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i For comparison purposes, a portion of the output listing for the period

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between 0.04 see and 0.0449 sec of each sample run is presen*ed in Figures i

2-2 and 2-3 t:ote that the listed results agree exactl'y. Therefore, it can w

be concluded that the RELAPS-FORCE modifications to RELAP5/ MOD 1 have not altered the internal thermal-hydraulic code calculations.

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2. Tee branch component volume length = 1 ft.

3. P1 = 1000 PSIA: P2 = 14.7 PSIA

5. Steam Quality = XI= X2=1.0 W

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7 3.0 HYDRAULIC FORCE CALC'JL ATICN VEP!?! CATION - EPRI /C-E PWF S?V TESTS

~I 3.1 The EPRI/C-E EWR SRV Tests:

L Under the management of the Electric Power Research Institute (EPRI),

a full scale ?WR pressuri::er safety relief valve test program was carried out at the Combustion Engineering (C-E) test facilities in Windsor, CT(3). The C-E test facility was desi5ned for full-flow 5

tests of selected safety valves under a wide range of inlet fluid conditions and inlet piping configurations.

Figure 3-1 shows an isometric of the test facility piping.

Ons of the objectives of this program was to obtain sufficient piping y

load data to permit confirmation of analytical models. Thus, the test

-1 facility was equipped with instrumentation to record transient 8

parameters such as valve discharge line pressures and fluid induced loads.

The EPRI/C-E PWR SRV Tests chosen for this verification are:

1. Test No. 1411: S eam Discharge

2. Test No. 908:

Cold Water Loop Seal Discharge

3. Test No. 917:

Hot Water Loop Seal Discharge llt These particular tests were selected because they all used the same valve model (Crosby 6M6) and piping configuration.

In addition, good l

quality test cata for nese tests is readily avauacle.

The test ata 4

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is su=arized in Reference 4. "Measurerents of Piping Forces in a Safety Valve Discharge Line' included herein as Appendix A.

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3.2 RELAPS-FCECE MODEL OF THE EFE /C-E CECS3Y 6M6 TEST FACI'. TY l -;

Appendix A, Figure 3 shows a detailed drawing of the test facility including the location of the process instrumentation. Force l

t measurements were made by summing the output of a pair of load cell strain gage trar.sducers per pipe segment (WE 28 througn WE 35).

l ihe RELA?5-FORCE mocel of the test configuration is shown on Figure 3-l 1

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tJote tr.at the nodal points for the pressure transducers used for k

the verification have been labeled in addition to the location and direction of the hydrodynamic piping leads calculated.

All the Crosby 9

6M6 tests were performed with a loop seal inlet piping configuration.

I The verification approach will be to compare the analytical results with the tests pressure and load measurements. Pressure comparisons are used to verify the accuracy of the RELAPS/ MOD 1 code and model in reproducing the test configuration physical geometry and transient thermal-hydraulic phenomena and thus adds further support to the force calculation validation.

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~1 3.3 COMPAR:30N BETWEEN RELAPS-FORCE CALCULATIONS AND TEST DATA 1

3.3.1 Test No. 1411, Steam Discharge Tests No. 1411 simulates a continuous stea= discharge through a PWR pressurizer safety valve. The valve inlet pressure was regulated by j

modeling the reservoir pressure to ramp frcm 2410 psia to 2540 psia in 0.5 see as indicated by Appendix A, Figure 6.

The Crosby 6M6 valve y

used for these tests had a full-open area of 0.0253 ft2 However, an

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area of 0.0204 ft2 was used in the RELAP5 model to achieve the test M

measured steady-state steam flow rate. As indicated in Reference 4, this valve leaked slightly Drior to the test and thus the initial downstream air was replaced with steam. Assuming constant enthalpy throttling, a quality of approximately 0.90 is calculated for the downstream piping steam environment. Therefore, the RELAPS model downstream conditions for this case correspond to 0.90 quality steam at atmospheric pressure and the pipe wall temperature initialized at 212cF. The valve opening characteristic model used for this test is depicted against test data on Figure 3-3 The full-opening time used was 15 msec. See Appendix B for a listing of the RELAPS-FORCE input for this transient.

L Figures 3-4 through 3-6 compare the RELAPS calculated pressures with test measured data for three discharge piping pressure transducers, PT 9, PT 10, anc PT 11 as shown on Figure 3, Appendix A.

Considering the pessible differences discussed belew, the calculated pressure histories are in gcod agreement wi:h the test data.

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5 The nycrocynamic piping forces calculated by RELAP5-FORCE for test No.

1411 are compared with the test data on Figures 3-7 through 3-10.

It can be observed that the magnitude and timing of the RELAP5-FORCE calculated Q

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forces agree reasonably well with the test data.

A notable discrepancy 2

occurs near the 200 msec point where test data for Forces 3 and 4 l

indicates force peaks not reproduced by the code. This difference is apparently due to the accumulation of condensate in the lower horizontal discharge piping leg prior to the valve opening.

Although, as discussed above, an attempt was made to model the downstream steam environment, information on the accumulation of condensation in the discharge piping was not available to allow reasonable modeling of this condition.

During the test, the accumulated condensate was apparently collected into a slug by the steam discharge producing the 0.2 see force peaks in pipe segments 3 and 4 as the slug of water accelerated out of these pipe i

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An important aspect to be consicered when the BELAP5-FORCE calculated loads are compared with test data is that the test facility pipe supports J

I stiffness was not high enough at some supports to allow a reasonable ene-j en-one comparison.

Appendix A, Figure 5 indicates that measured loads on pipe segments 3 and 4 should be expected to be somewhat below the actual support applied load due to low supports stiffness.

In this regard, it should be indicated that the force comparisons herein are intended to verify the adequacy of RELAPS-FORCE for hydrodynamic force calculations.

They are not to be considered as a s.ibstitute for the piping structural analysis re:;uired to cetter reproduce test loac data for pipe segments with low suctorts stiffness.

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3.3.2 Test No. 908: Cold Water Loop Seal Discharge "1

' Test No. 908 was performed with the loop seal piping filled with cc1d water. The valve inlet pressure was regulated by medeling the I

reservoir to de-pressurize from 2690 psia to 2670 psia in 0.5 see as E

indicated by Appendix A, Figure 16.

For this test, a 0.0834 ft2 orifice installed at the exit of the 12" disenarge pipe was modeled as a RELAP5 abrupt-area-change junction of the same area. As in test No.

1411, a 0.0204 ft2 full-open area was used in the RELAP5 model to 7

achieve the test measured steady state steam flow rate. Appendix A, Figure 15 shows the loop seal temperature distribution prior to valve opening. During the initial opening phase, this valve chattered appreciably for about 0.9 sec. before opening fully in about 15 msec.

Therefore, the loop seal water was discharged into the outlet piping prior to the valve's full opening. For this reason, the RELAP5 model c,

includes the loop seal water volume distribution in the outlet pipe and a 15 msee linear valve opening characteristic as shown on Figure 3-11.

In accordance with Reference 4, the downstream piping initial conditions were set for 800F air at atmospheric pressure and an assumed relative humidity of 907..

See Appendix B for a listing of the RELAPS-FORCE input for this transient.

I Figures 3-12 through 3-14 compare the RELAPS calculated presst.re histories with test data at the location of pressure trancucers ?T 9, PT 10, and PT 11.

The calculated pressures agree reasonably with the test data with two exceptions.

First, the PT 9 pressure test cata exnibits an off scale peak en or about 25 msec believed to be of I

I

spurious nature. However tne calculated peak pressure at tnis location occurred much earlier into the transient than the seemingly valid test data indicates. This difference is probably due to the initial discharge piping loop seal distribution discussed above.

Second, the RELAP5 pressure histories at the locations of PT 10 and PT

• • agree well with test data in the early and latter parts of the transient but exhibit a depressurization between 0.10 anc 0.25 sees.

(

Close scrutiny of the RELAPS results indicate that this is due te a depressurization downstream of the vertical discharge pipe's area l

change due to supersonic phasic velocities. This behavior is produced by the absence of choking at this area change during obvious chcking conditions, i.e.,

fluid velocities larger than propogation velocities.

j As discussed below, a choking model was not applied to this area change junction to prevent underestimating pipe segment 2 loads during l

~

the discharge of this cold loop seal slug. As the loop seal water is cy discharged out of the piping system, steady state steam choked flow at the discharge orifice plate recovers the PT 10 and PT 11 pressure to the test measured levels.

J The hydrodynamic p.iping forces calculated by RELAPS-FORCE for test No.

908 are compared with test data on Figures 3-15 through 3-17 The magnitude and timing of the calculated loads for segments 1 ar.d 2 compare reasonably with the test data considering the loop seal location modeling assumptions required by the initial valve chatter.

The higher calculated segr.ent 3 icads can be attributed to the relatively low stiffness of this segment's supports which decrease :he test measured loads. The segment 3 caleui.ited loads. nowever. seem a

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reasonable since the resulting forcing function is expected wnen compared to the calculated and measuced loads on the stiffly supportec segment 2.

It should be noted that the enoking model was not applied to the expansion junctions on pipe segment 2 to orevent I

underestimating the loads on this segment due to the lower E

acceleration of the' loop seal slug as choking occurs at these i

junctions.

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RELflPS-FORCE VERSION 14 - GILDERT flSSOClflTES 1140. NOV. 1983 EPR1/CE SRV TEST NO. 900 J.M.CflJlGils RSF/1-14 27/02/04

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3.3.3 Tests No. 917: Hot Water Loop seal Disenarge Test No. 917 was designed to simulate a hot water loop seal discharge' Si=ilar to test no. 908, this valve enattered for about 0.65 sees before opening at 2650 psia in about 90 msec. Therefore, the RELAPS model includes a 90 msee linear valve opening characteristic, Figure 7

3-18, and 0.5 see inlet pressure ramp from 2650 psia to 2720 psia corresponding to the reservoir history shown on Appendix A, Figure 26.

A RELAP5 model valve full-open area of 0.0194 ft2 as required to match the steady state steam flow rate measured during the test. Per Reference 4, downstream initial conditions were set for 80c F air at atmospheric pressure and an assumed relative humidity of 907..

See Appendix B for a listing of the RELAPS-FORCE input for this transient.

I Figures 3-19 through 3-21 compare the RELAPS calculated pressure histories with test data at the location of pressure transducers PT 9 and PT 10.

The calculated pressure histories are in reasonable agreement with the test measurements. Although the peak pressure measured at PT 9 was higher than the RELAPS peak, this maximum occured at the time the loop seal slug was passing this point which resulted in oscillatory pressure measurements. However, the average of the PT 9 peak pressure oscillations is in good agreement with the RELAP5 I

calculations. Agreement between PT 10 test data and RELAP5 is good except for the period between 0.2 see and 0.5 see where a supersonic velocity depressuri:ation phenomenon similar to the one discussed in section 3.3.2 occurs. Consistent pressure recovery starts at acout 0.35 secs with stmdy state choked steam flow at tne e.it no :;e I

I The RELAP5-FORCI piping force histories for test No. 917 are compared witn test cata on Figures 3-22 through 3-25.

The magnitude anc timing of the calculated loads are in good agreement with the test data with some exceptions. The segment 1 force function behavior indicates an I

e oscillatory period in the early part of the transient. These oscillations, also shown in the PT 09 pressure data (Figure 3-21) are the result of the valve chattering ocserved during tnis.est.

This resulted in an oscillatory opening and closing pattern during the valve oper.ing period. These oscillations were not modeled into the RELAP5 valve opening model and thus the pressure and force oscillations induced by this condition were not reproduced by the code. Slightly lower segment 3 measured loads are attributed to low supports stiffness (see Section 3.3.1).

n wave contribution positive peak at about 0.22 see was calculated for the segment 4 force history I

but was not measured by the test instrumentation. A review of the U

RELAP5 results indicates that this behavior was expected since the I

3 wave force peak corresponds to :he time of loop seal slug acceleration h

out of the segment 4 section. The segment 3 force test data indicates g.

that the slug was still intact as it left this segment and thus a J

segment 4 wave force benavior like the one calculated by RELAPS-FORCE is expected.

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O 4.0 HYDRAULIC FCRCE CALCULATION 'lERIFICATIO!:, EDWARDS' AND HA! SONS' PIPE EXPERIMENTS q

4.1 EDWARDS' PIPE EXPERIMENT Tne pipe clowdown experimental cata reported by Edwarcs(5) in 1970

'l provices an excellent experimental data base to cenenmark the blowacwn force option of RELAP5-FORCE. A sche':atic of the experimental i

facility is shown on Figure 4-1.

Note the pressure of gauge stations (GS1 to GS7) used to measure the transient pressure, emperature, and

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void fraction in addition to the load cell used to measure the hydrodynamic pipe axial load.

I The experimental tests consisted of pressuri::ing the pipe with water to the required test pressure and rupturing a glass disc at the end of the pipe with a pellet gun to initiate the blowdown.

It was observed that some of the glass disc was retained around the circumference of the disc support assembly reducing the discharge area by as much as 157..

The test used for this verification was initiate,d with water conditions of 1000 psig and 4o70 F (saturation pressure = 285 psig) 5 4.1.1 RELAPS-FORCE MODEL OF THE EDWARDS' PIPE EXPERIMENT The RELAPS-FORCE model of the test configuration is shown on Figure 4-2.

RELAP5 output data requests (minor edits) wer e selectec for those volumes corresonding to the gauge station locations and for tne pipe wave, blowdown, ant tota' fcree ca;culated.

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The verification wi;. consis of pressure. :e:perature, voic fraction,

9 and load comparisons ce: ween RELAP5-FORCE anc :ne test cata.

As indicated in Section 3.2, thermal-nydraulic parameters such as pressure will alicw verification of the RELAP5 ccde and model accuracy

.s in reprocucing *.ne test configuration pnysical geometry and thermofluid trr.rs;ent phencrena in support of :ne feree calcula:icn valication.

I Note that to simulate the test observations, the RELAP5 model discharge junction area has been set at 0.03835 f 2 or 15% smaller than the pipe area. The RELAPS-FORCE input listing for this problem 1!

is included in Appendix B.

4.1.2 COMPARISONS BETWEEN RELAPS-FORCE CALCULATIONS AND TEST DATA, EDWARDS' PIPE EXPERIMENT 51 Comparisons between the RELAPS calculated thermal-hydraulic parameters and test data, Figure 4-3 through 4-5; indicates good agreement between the experimental and calculated results.. Ex.cellent agreement J

is also indicated by Figure 4-6, where the measured end thrust load is l

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u.2 HA!!S0!J'S PIPE EXPER*ME!;T t

Another excellent source of test data of blowdown fluid thrust forces

]

is co.tained in a 1970 report by Hanson(6)

The experimental ecnfiguration of this pice experiment is shown on Figure ;-7.

Althougn experimental pressure measurements were mace, PS' to PSL, this cata was not available in Reference 6.

i y This " pipe break" experiment was initiated oy over-pressari::ing a i

I'-

rupture disc at the exit a 1.1" ID pipe with a positive displacement pump. Tests were conducted with and without exit orifice plates of 30; and 107, of the exit pipe area.

4.2.1 RELAPS-FORCE MODEL OF THE HA!!S0!J's PIPE EXPERIME!JT i

i 1

The RELAPS-FORCE model of the experimental arrangement is shown on Figure 4-8.

The initial water temperature was assumed as 800 F vs.

l the test's 600 F to avoid early abortion of the RELAPS calculation due to a " water-property-error." This a::sumption should not alter the results significantly since both the density and sonic speed for both l

mediums are e::sentially the same. The reported rupture disc opening time of 0.35 mnec was modeled with a linear characteristic opening of 1p-,

1 a RELAPS " motor valve" (MTRVLV).

Similar to the Edward's expertment, the verification approach will consist cf a co par!aon bet-cen the test data and the RELAPS-F0fCE

?lI0Miat{0NU.

DeedVer. 2F[Y i.D 1 rol{ ddta

.M

.Wallibid I 3l IP i' l

l

I

~],

I comparisons. Thb FELAPS-FORCE incut listing for this problem is incluced in Appendix B.

l 4.2.2 COMPARISON BETWEEN RELAPS-FORCE CALCULATIONS AND TEST DATA, HANSON'S i

P:PE EXPERIMENT i

Figures 4-9 througn 4-11 snow the RELAP5-FORCE calculated forces and the test measured data for the 3 different pipe exit area experiments.

The agreement between tne experimental and calculated transient forces

[

i i

is very good with respect to magnitude with small deviations in timing j

due to slightly high RELAP5 calculated sonic velocities.

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Dist WM YM M e LCNGTM OF SM ALL PIPC, INCHES WITH NO CMTENSION 88 INCMCS l

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OMIPICE PLATC IS MEMOVCD POm STUDIES WITH Pub 6mOpCN SMCAe(,

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• 0'I I

The conparisons eeween RELAP5-FORCE calculated loads and test data discussed in Sections 3 and 4 indicate that RELAPS-FORCE can provide good en61neering estimates of hycrodynamic pipint forces produced by fluid transients.

snould ce indica:ed :na: REL;P5-FORCE simply l

performs the required computations to calcuhte the nydrodynamic force g

histories from RELAPS ou:put parameters and thus the accuracy of the resulting forcing functions is greatly dependent on the RELAPS modeling experience of the analyst.

Y I

t W

W I

I I

t

I 4

6.0 REFEFE"CES

1. RELAP-FORCE User's Guide, November 1983, University Ccmputing Co.

1

2. Ransom, V. H. et. al., RELAP5/ MOD 1 Code Manual Vols. 1 and 2, EC&G Icaho. NUEEG 'CF-1826. March '981.

I

3. EPRI/C-E FWR Safety and Relief Valve Jest Program. Summary P: ogram Description. EPRI. 1980.

I' 1

j

4. A. J. Wheeler and E. A. Siegel, " Measurements of Piping Forces in a l

i Safety Valve Disenarge Line", ASME Paper No. 82-WA/NE-8.

[

i

5. A. R. Edwards and T.

P'. O'Brien, " Studies of Phenomena Connected

)

.{

with the Depressuri::ation of Water Reactors," Journal of the British 3

Energy Society, April 1970, Vol. 9, pp. 125-135.

6. G. H. Hanson, "Subcoolod. Blowdown Forces on Reactor-System

.)

f Components: Calculations 1 Method and E:;pertr.cntal Confirmation,"

i IN-1354, June 1970.

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02*WAME-8 g

THE AMERICAN SOCIETY.OF MECMANICAL ENGtNEERS l

us E.a si

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$.'t nm.

no am.1.r iscal Div.

n.

t. th. enNt.fi P

r..r. e va trom AS481.

I S*Teret.fh tsh$

ennee.us4.

?

f l~ !

l MIA5UR! MENT 5 0F P!p!N3 FCR:I5 IN A SAFITY VALVE C110tARGE LIN[

A.J. Wneeler Project Manage

• Ele: trit So.ee Researer Institute palc Alte. California E.A. Siegel P*incipal huclear Engineer Comoustion Engineering, Inc.

Windsor, Conne:ticut f

I M1TRA7 ne:ted to the pressuriter such that the

• inlet to the j

valve is esposed only to staae. In another c trion i

measurements were made of support reactions to design, the portie s of the pipe tancediately upstrean transient hydrodynamic forces on the dittnarge 11ee of of the valve contains 11ould water. This design, a nuclear reactor safety valve test facility. Da ta corrionly called a loop seal design (Figure 2), is used is presented for three different test conditions.

to minimite leakage through the valve seat. When the two with upstream 1000 leals and one with only steam.

valve on a loop seal assign opens, the watee is pro.

t luffittent information is provided to permit verift.

p.lled down the discharge line ahead of the steam, cation /devoletrefit of hycrodynamic forte predictive Due to its hign sensity. the water produces signifi.

moests, cantly higner loses than steam alone. The (PRI pro.

gram obtained piping loss data from configuratiovit

!NTR3 DUCT!CN coth with and without loop leals. This paper presents cata for three tests = an all steam telt and two loop For worte* safety and operational reasons, the seal tests.

steam distnarge of nuclear reatter safety or relief valvet is norr. ally routed througe pipes to a tant of m4

,4

.aie, watch ouentnei tne ites.. Wnen tne valvei..en, the atteleratton of the fluid in the discharge pipe causes tutstantial trantievit loadings which must be restrained with tuttable piping supports. Istima tes of the transient loadingt are reoutret in order to

' to es.in ta.

l detign these supports.

,,g, Althougn analytical methods to predict taese loses have been available for some time, the esta e

paie to.en an oe.emd ha. ooi.een e ieniive.

--t and ignificani once tainiy na esi ied in premied i

loads. As part of a retent safety and relief valve test peogree for p*etturtled water reactors (PWR't) managed by the [lectrit Power Besearch Institute

((PRI) and sponscred by the utility owmeet of pret.

\\j turned wate, reatters, sa espe 1..ntai diitnerge I

iime w.

initru..,ied wit, iced ten, ai ihe tup,o i.

to e. tend i e data sais. thii ps.t. dotu.enii se, tests pe* formed with the Crotby 6M4 lafety valve, the most ters.on valve Wied on NR't.

p]ggag 1. getts, gr NR In tne pressurised wate* reatteen detien, tne Pestter safety and Pette' valves are come**ted te tne prentweiter, a reellure tellei sontateleg tota este*

and itene w*itte it used to tomtrol t ytts.* r'etture

( figart 1).

IP te*tain trennteatl. Ites* 'l *.lested D*aven t*e ta'ety sa reite' valvel 1.

'im't tne 196 ter p*entu et le its.e set tgal, tre o >ve #*e ta*.

I a

I

foue segments is sucoorted at one end of that segment in tne antal direction. A design goal for tre test facility was to *ninimize or altetnate load oath re.

~

danoancy for all discharge oising loads. This goal I

has eeen attained by providing arial pine succorts wntch are very stiff comoared to alteenate load caths.

minnaar The elimination of load oath resuncundancy has been conf tmed by cynamic analyses as part of the overall sit"'

design effort.

V tach segment of the pipe was sumoorted with two f= \\

load cells, ar*anged in carallel. The net axial load l

l T

I on each segment is the sum of two loao cell measure.

ments. Data was retorced witn a digital data accuisi.

tion system untch samplec tne load cells at a cate o'

(

W 1000 samoles/seconc to allow *esolution of vo to 200 MI. Tne measurements are accurate to ;,2200 h.

Static oressures were measurec at several down.

stream locations three of which are cresented meet.

eT09. ST10 and PT11. Tnese instruments we*e also I

1 F13URt 2. PwR LOOP S!AL DI11GN samcled at 1000 samoles/second to sllow resolution o*

frecuencies up to 2',0 MI. The accuracy of these mea.

surements is + 28 tras novever, the sensing 11aes.

The primary objective of this paper is to make unich are aoovt one mete

• long and filled with cold f

data avatlante to indiviouals developing or verify.

water, eight tend to reduce tna accuracy at hign fee.

ing mocels to produt piping loads.

ouencies.

TIST FA:! W Three other incoetant measurements are valve slow-The test fact 11ty (rigure 3) consists of a fou, rate. valve, stem posttien anc uestream rese.voir tana j

pressure. ihe valve floweste was measured with a segment dischar e line attacned to a spring. loaded venturi wntch is only accurate under steady or close safety valve.

h all cases presented here, the to steady conditions. In the test facility these con.

piping unstress of the valve =st a loop. seat designs attions occur a few seconds af ter the valve has open.

i I

however, the loop seal water was drained for the all.

ed. This measurement is accurate to about : 65 of I

steam tests.

reading. The valve stem position was measured at ect.

I ly with a Itnear velocity and displacement transducer.

l This instruneet, accurate to

• 0.13 mm, was also samel.

l w

u w.,

ed at 1000 samples /second. tee upstreas vessel pres.

sure presented here is pT12. an instrument samoted at

• • u 3 r

/*,,,,

100 samoles/second to allow eesolution of frecuencies M

up to 20 MZ with an accuracy of 3,69 kPa.

" '"c y o.

g#

For loop. seal tests, the temperature of the loon viensi t '8 l $.

seal water is significant. If the loop seal temoees.

I ture is high enough, the water util flash as it pas.

ses througn the valve reducing the measured down.

stream loads apprecially. Two themocouples were "7*

utilised to measure loop. seal fluid temperature direct.

I 88 I

ly.

In sedition, seveest themocouples were attach.

ed outsice the pipe to measure wall temperature. It ene is espected tnat these mestueements can be used to de.

e mac 4 W

"M.",d, duce the flute temperature antal distribution.

I STRUCTURAL IFFICT1 IN THE MIA1UntD LOA 01 ameu""

,,, u.

num.

Wnen any structure is subjected to dynamic loads.

)

87

$a it =t11 retooed in a manner that may atther amplify I

-u%s,",,w,,ieus or atminish the applied dynaatt loadteg. This escoct

=r of dynamic response characteristics of a structurel F 7 support system is referred to as transatssittlity.

/ L8 Transmissibility is defined as the ratio of the sup.

or I

poet load to the apolted load. The magnitude of this ratio is otoendent on the relationship of tne cyc1tc

• 8" "

'resuency of the soolied load and tne natural frecuency r e an in inttely rigid structu e, o

e r

of tne structure,

""I' f!;ust 3. ftli FA 1LITY (1 f t.*0.30ste) nesses. no= eve"r, tnis catto can to signtf tcaetty aeove I

T>e hydraullt loses act in tre estal direction in itscPaege otpe serinents, taen of tne each of tne fov e I

9 t

I g>

Ve'ification or evaluation of a fluid model for g',

predicting nyorocynamic loacs uses a process uniCn is l

• 1 similar to the application o* ine same code for oower I<

e is a

i plant otsign. First, the fluid code is used to credict the hydrodynamic loading on the insidt of the pice.

/, _.,_

i Nest tne nyorodynamic loadings are sed as forcing.

sa 1.!,,,,M,,

function inputs to a transient structural model of

h. r.n{

the piping. support system. In the case of plant j

design, tne resulting support loads are used to design a m %y g/

l the supports (probably witn structural reanalysis),

is,

-u In a ve*1fication effort, tne support loads are com.

3 i

pared to the test data to evaluate model adecuacy.

!s 8'J'y' I*

"g== w.s i

e,'"...

t j

The loaa cell instruments es not measure the I

....,g

-f fluic loacs directly out ratne-tne response of tne 3

R

1ptng-supoort systea structure. Every attemet was l

8 maos to coastruct the facility so snat the supports I

were very stiff so that tne load cell measurements

,J were as close as practical to tne fluid forces.

7' heve-theless it is necessary to include a model of

3 I[l 2

3

ne structure to fully valtoate flute loading computer I',

codes.

In order to design the test facility. 4 detailed

'l-structural socal of tne wnole facility was developed.

m 5

\\ ml, /

Based uoan test data anten gave information about tne

[

natural f recuency enaracteristics of the f acility.

==

the structural model was adjusted to represent tne m.

as. built facility. However, not only is that model much more elaborate than is recuired to evaluate um g

disenarge piping loads, but a esta11ed description

~

,r.ri eu e

of tne model is beyond the scope of tne present paper.

t As a result, a simplified structural model based on tne more complex mooel has even developed. This FIGURI 4 - PRES $URE YESSEL. SUPPORT SKIRT model consists of the reservate pressure vessel, the AND VALVE INLET PIP!NG (D!MENSIONS IN INCHES,

}

}

valve, the discharge piping and **ie piping supports.

(

The required dimensions for the tant and valve is (1 INCHa26.4 m) shown in Figure 4 (ach of tne piping suoports is taas teu tocanyt

(

represented by a spring or springs as shown in Figure w me.

ant es.

I g

at to i

p 5.

The second third and fourth segment supports l

{

attach directly to tne concrete basemat. The first segment supports are attacned to a beam structure sj g

sy wn e.

~~

in ~ a n. %

unich in turn is attacned to the reservoir pressure n

n vesiti, ror structurai mocei purposes, sne beam a

j =.ru itructure mais is appro.imateiy so7o.0 =g and incated n:;

e at sne top of sne pressure vessel. The nexibinty r

a M'i.wnia ewe of the bene structure is incorporated in the stiff.

i

• " Y""'"""

ness of springs 1 to 2 and 3 to 4 in Figure 5.

The e'i ewn En vessel in turn is cantilevered from the basemat. It

\\b

.e f,s,l,=*w u m 3

is censidered necessary to model the pressure vessel H w sease it e (:p*sturen and stirt stiffness and mass in order to provide a 8 "*

einimum system model.

M 886 "

i.t a. ss.m.o p',,

50 Tc7 RtsuLTs 9

L8 o

f a The results of three representative tests are re.

ported here. These tests are distinguished primarily

• [

u

)h,

,3 8*

by the inlet condition to the valve. The tests pre.

/

0 sented aret ss,o 3sss s

,s steam only. Test 1411 FIGURE 5 37!FFNt15 0F P!P!NG $UPPORTS Steam with a cold loop seal Test 908 (1 lbf/in=0.176 h/m)

Stese with a hot loop seal. Test 917 1!

m of these sesit.e.e pe,f-ed.iih a,aive manuf actu ed by Crosey valve and Gage Cosecany, model 6

a 1

MS.sp.46.

It nas sin inen (15! m) inlet and disen3rge NaPies.

f>* valve hat a me g 21 e a P88 o f

• 35 i 10*

• • 464 an CMI estee flow of 161.615 eg/ne esta 17750 l'a sat. rates steam.

5 3

1 I

I Tett 1411 Figures 8 througn 11 present the measu*ec forces g

on each of the four pipe segments. The peak forces This test was performed with the loop seal 007 observed on segments 1 tnrougn 4 are 11565 N. 23912 N.

I valve was exposed to a steam only inlet condition.

tion of the inlet piping drained of all '1ould so the 53,376 N and 66.720 N respectively. The peak forces on segments 3 and 4 are somewnat delayed. These Prior to the test, the valve was leaking slig?tly.

pests are thought to De caused by condensate (result.

9 Thi) acceared to neat the downstream pipe walls to ing from pre-test steam leatage) striking the elbow 100#0 and reolace the air with steam. The cuality just upstream of tne pipe discharge to atmesonere.

I of tne cownstream steam is unknown.

The pressure history upstream of the safety valve

,Zl.[!

I l

1s shown in Figure 6.

The safety valve popped open I

wnen tne tant pressure reached 2410 psia.

,{;

The valve

=

stem position Mistory is snown in Figure 7.

After the 3 ;

initial transient nad sucsioed. the cuasi. steady flow

^

~

l a

l I

nrough the valve was 213.145 mg/nr wnen the tank I lf I $ ' ' f.k ' /

2 I

p* essure was 18234 kPa.

Em

-L f

h 0 I ff

\\--

• N's

,_.,.nl....i..

j i.

q q

vv,i

)

I l

!_l is I e a

i

-. e a

._ i

. i..

e l

y I.

e I

n.n n.

n.ra

u. sz A

.-. i i

StComet 8.

i

[

ji ~-

".~.:I. l i

FIGURE 8. TEST 1411 $t*. MINT 1 FOR ! HISTORY I

.t

.. [;

(1 lbf=4.448 N)

E

.._ ),.. '

m _. 4,_ __.

p..

l I

ro.e ts.e 34.s as.e

$ttImes FIGURE 6. UPSTREAM RIstRVOIR PRES $URE M1370RT p

(1 pita =6.894 kPa)

I

~

1 I

-i_.,,._.._..

g g p np.._-. q..,.g 9

g.-

=e

.:- __.T...

_; :.:n I t=._

I ra-l c3 Ll m

i d

-u

-- :.=1 ~.._ill.;O

. L.=.*_._

--~

=

L y

+--?-F@h g.y !h i 3 {j,, g._,f) H, p g

l mE=!!.EF.i.L :h d' J r$' k

.-- = ++.2 :- u

il

_n r

. 0

i --

9:

I 3

i

=

g

-j l. ' '. l f., I

... f.

.l.

l l

l.

23.28 H. 44 23.76 23.92 I

33.14 t).!!

. U. 44 23.sa gg gs.g sace=os t

F! CURE 7. TEST 1411 V4LVE STtM PC1! TION. II26 Ft;gRg g. Tr$71411 st.utNT 2 FORtt HISTCRT (1 intn 21.4 m)

(1 lbf 4.448 N)

I I

O t

$'f

]

{

~

d b

~ ~ '

~ p

=

o 1

A i<

3

- - -.-I 3

_..p-. _L.._ i,_.. -

i..;.

g

.. '.!.~

i k

...E1.

l. N --

I 5,,

/

g :,

_....{.

i 3

4 __

y

.4 4

f.

g

' Tf,

l

[.-

{#

v)! g-o t

A

+

l 3

i I

3 3

g

g/

23.28 23.44 23.so 23.7s st: ens g;

23.2s 23 44

3.so 23.76 FIGURE 12

• EST 1411 STATIC PRESSURE TAP st:cus PT09 RESPONSE FIGURE 10 - TEST 1411 SEGMENT 3 FORCE HISTORY (1 lbf=4.448 N)

R a

+

^ A.i.

i V

=

~ 8 ji

! l.

'S

---

i 3

i

.. I._h.,!

b g

y i:

i

- y'

=3 4.

_H.

_. p._

u j

==

_4 g

4 p

s

.__._4.-.m.

- u -._;

i 5,

+ - -.- i --. i n.

^ Y - i--'_.!-~'_1. ) '._- !M rI.2s

~

23.44 23.so ts.i

=

.. i...._. p.._ _ p.

E i - t-stecns

.a.

- _.. 4 :

j_

FIGURE 13

• EST 1411 STATIC PRESSURE TAP

_t e

_4_

.r,.

PT10 RISPONSE

-;_._...u.

.g (1 psia =6.894 kPa) 23.ts 23.44 23.so 23.7s st: ens 2

FIGURE 11 - TEST 1811 SEGMENT 4 FORCE HISTORY

? l!

II 5

g g}!,

(1 lbf=4.a48 N) 2 h '

E

'i Although not a measure of force, static pressure data is also useful to validate analytical models of a2 yy f..

1 IN piping hydrooynamics. Pressure cata taken at taps 3

1 P PT09, PT10 and PT11 are presented in Figures 12 5

Inrougn 14. Ten seconds after the valve popped ope 9 w

at r -

.:{ *$ l'y i

and the flow was ouasi-steady, the tank pressure was 3=

16994 kPa. and these three pressure taps ave read-I

.c=

ings of 1551, 738 and 738 kPa respective 1 (not shwn g

.)l l

on the Figures),

g j

Y',' ~f 1

f Test 908 I

inis test was performed with the loop seal pip-3

' al i

in9 filled to the top with cold water. The tempera-

• ure measurements are presented in Figure 15.

For

$.2a 23.44 23.50

+3.'s 8l this test (but not for 917 or 1411) a 99.3 m diameter stms orifice was installed in the 12" pipe just upstream The downstream pip-of the distharge*to atmosonere.

ing was at 15-38 : prior to the test.

IGURE 14 "EST 1411 STATIC PRESSURE TAP D'11 RESPCNSE (1 esta=6.894 kPa) 5 I.

i I

t ur w....

4 m.mv l

u-mq f-X I

s

• =

E E l.:

E = _--W o

=).

I L

i=

N.,/

• s

~

E s

m. n.s 3

-;y i

9 e. nem I

O V

=!

r,

=

4 m

g i :

br

=

• er'

= -

f.r. = :-l__..

'e'

- =

w I

C

~

~~~~

FIGURE 15 - TEST 908 TEMPERATURE PROFILE g

IN LOOP SEAL

,i (tc=(tf-32/1.8)

Es

=._ h Ikt

.a._.

a I

The tank pressure history is presented in 22.00 22.so 23.sc 34.4:

Figure 16. The valve-stem position data (Figure 17) maes indicates tnat the valve did not simply pop open as in test 1411 but instead oscillated for apout 0.6 seconds, FIGURE 17 - TEST 908 VALVE STEM POSITION lE17 l

I remained partially open for about 0.3 seconds and tnen (1 inch =25.4 m)

-d popped fully open. This type of benaviar was observed on most of the spring-loaded safety valve loop seal tests run during the EPRI program. The flowrate was g

210,900 kg/hr wnen the tank pressure

=g I

observed to be rate is the steam flow in the outsi'-steady condition y.

--i-l h'

d

,}

~j

(

was 18545 kPa psia. In this and test 917, the flow-

._u 01 af ter the loop seal had Cleared the valve.

g6 g.

\\

!-- !} J

)

I

~~

--I l

h

=

J. \\..

-e t

g5 v.

o r-e i

I i

_ p....;

.j g

i d

I

.s

• y j

..-i -~

i. ~..-. i.

.N o

j

.,_ j l

~

3 $.

E g

[

g i

e I

}

. ~

p.is u.23

x. 31 M.3s

=:3 g

1 ;.... p..

stconos

-i FIGURE 18 TEST 908 SEGMENT 1 FORCE HISTORY E*

i T

(1 lbf=4.448 N)

$j

. j i

l t

o

.a 4

30.0 3a.0 46.0 54.0 o

I I

-'*U~~

~.

stconos

_5--_.--.

-... -.-. / k [ ' k n[;.f { P FIGURE 16 - TEST 908 UPSTREAM RESERVOIR h

- ~

• y N (

- ~ - - - - I-v PRES 5URE HISTORY

. _. _.. ' * ! d ; I (1 psia =6.894 kPa)

!2 V

-3 l

0' t

t : :, v

,-giu i

The observed forces on each segment are shown

-.--i I

''I

in Figures 18 - 21. The observed peak forces on seg-2

~ ~ ' ' '

ments 1 througn 4 are 97,856 N, 800,640 N, 266,880 N g

i- -.. j i

800,640 N load appears to be g

I and 88,960 N. The large caused by a relatively intact water slug striking the

~g

- tf second elbow. No such large load is observed at the u

Shird elbow - the slug may have partially dispersed i

j by the time it reaches that point. On the other hand, 5

a large load at elbow three may be masked by a combi-E I

l nation of the structural sof tness of the segment 3

.4 1

supports and the discharge orifice and short length 5

1 I

of segment 4

'34.1 s M.23 3a. 31 34.39 l

sttomes FIGURE 19 - TEST 908 SEGMENT 2 FORCE HISTORY (1 lbf =4.44S N) r I

=

6 l

l a

l

3Il 1

\\*

'o

~a

_i....,

}

'" l ~~.' ~ ! '

i

{

E,

~.

[

.,.p r, -+

4 7

.)

t

=

I) a

--.i -

i i J jl t

~.

~ ~~ !.**.

'p, [ ' i } !{.I E

-i-l-i L

}'

j iE p.j a

\\

. ~ ~ji.. - ;

.[

'.l E.

l

- f _A -!

=

g f] k.

i 2.

ti i

3

_ i.

.._ - - + 4._...

4...

g,

-T

..i s u.:3 u.n u.n E

}/

l st:m s e

p.15 x.23 M.31 x.39 FI;gRg 22. TEST 908 PRESSURE TAP PT09 RESPONSE

~'l st:ms (1 psia =6.894 kPa)

I FIGURE 20 - TEST 908 SEGMENT 3 FORCE HISTORY (1 lbf=4.448 N) a E*

! - i -.. i -. i 4~j #

3

.9

_3 q._

j.

-i --t p.-3..

,. __--;._._.._ c,. y.

j~~

5*

j.

l-

...j

.}

g l ' ;,- - {

,-~&

..-..i_.

g l

y. ~ r.

3.

a._.

t 4 - -,

. 4 8..L y i

...J.4...

E

_ i.- i -

.. j I

L l

ja4

_4~

._g - j

$. [-

.., j y*

[-.b) j li '

• M.1s 4 M.23 s4. 31 M.39 l

g 2.~.iE_.;

7~.J.

.' y stems Y

I

-.-;.4-

i. l i

. -.4 i-~l-FIGURE 23 - TEST 908 PRESSURE TAP PT10 RESPONSE m

f I3 4

(1 psia =6 E94 kPa) p

.s 7,

}

3a.1s M.23 N.31 M.39 E

sicmm.

qg 3

i i

I FIGURE 21 - TEST 908 SEGMENT 4 FORCE HISTCRY (1 lbf=4.448 N) 3

.i The static pressure measurements for PT09, PT10 EI 4

~

and PT11 are shown in Figures 22 - 24 Not shown on g

.j..

}

f the figures, unen the system had been flowing for g

i aoout 10 seconds and the pressures are cuast-steady, m

w; these pressures reached values of 4481., 4481. and i

i t

4550, tPa wnen the tant pressure was 16,959 kPa.

El 5l x.1s x.23 m.31 M. 39 Test 917 stems Inis test was similar to test 908 except that the loop seal volume was filled with fairly hot (1770C) water prior to the test. It was expected that this FIGURE 24 - TEST 908 PRESSURE TAP PT11 RESPONSE euld reduce discharge piping loads since flashing of (1 psta=6.89 kPa) f' the 11ould would disperse the downstream water slug.

The temperature measureents on this slug are shown in Figure 25. The discharge piping was at ambient Figure 26 shows the tant pressure history.

I temperature (10 3eoc) prior to this test. The valve Figure 27 showing the stem position, indicates that flowrate was observed to be 204,075 kg/hr unen the the valve oscillated much the same as in test 908, I,

tant pressure =as 16,821 kPa.

B 7

I

I Tne segment loads for this test are c*esente: tr

~1;ures 28 - 31 The ecservec peak loacs are 3',125 %,

66,720 N, 77,840 and 65,386 N on segments i throggn 4 resce:tively. These represent s1gnificant re:gc.

]

• g ".g',"

I mel tions in loading relative to test 908, particularly m;e

.. n on segrent 2.

m.m

,tip )=

\\/

...m.

, gig

~,

I

/]

U,,,

=. _ =,,,,

=>9 we.

...m

, a. l

=

e

=

L

)

5

• lAY h.d [l j % J : i,l or k.' j,

? d im..e y

.j b, i,t I

2 q.iq

'l '

y e

i '- r-. \\q'y.

[J, y J O g t RGURE 25 - TEST 517 LOOP SEAL TEMPERATURE PROFILE g

,l 3

pil Ii (t = (t -32)/1.8) t 9.i k:

u g

f I5

i. 7 3

.,. 1 :

d) l

,{

3 J

o-

_)

./

I

-3 j

1 71s.1o is.2o is.Jo 18.40 E

1 ums

[

- [ ' ;, '..'. t j

RGURE 28 - TEST 917 SEGMENT 1 LOAD HISTORY I

(1 lbf=4.448 N)

J e.

i-i 2

i I

l

=

f._.:~[.]~_

~

3

.I I

2 3

1 3

,8;.-

__.q. - r.

3 j

=

g L

z.

.p.n

.,l i

- o s

. i -.-

4 V Ai r,

J; j

4

{

g%.--pyrj-y1

. -i

~

I

..,, p g-p yl 1

g I I, ' ~~--i-- ' u~ - -' - Aj {,; *. N b.

- J It j

l 12.0 22.0 32.0 42.o c---

- i -v ~ r stconos a.

E = -._ - +._. ]._

y i

H I

FIGURE 26 - TEST 917 UPSTREAM RESERYOIR 3

-~

'/'

M

~ ~ ' ^ ~ ~ ~

PRESSURE HISTORY 5

IW (1 psia =6.894 kPa) c:

-i q

,3..

_..q._..._.

,g I

~

2.

7.....

y d.[

Is.10 1s.zo is.30 is.ao j

I ia

._i.

sta:s g

Tg i

i 9.

P-FIGURE 29 - TEST 917 SEGMENT 2 LOAD HISTCRY (1 lbf =4.448 N)

C j..

j E g

E e I,

c The cressures at PT09 and PT10 are shown in j

I*

I

' 5 f

=

t' Fioures 22 and 33. Ten seconds after the start of the transient, these pressures hao values of 1585

~ i I ) U # _lI E

and 745 kPa when the tank pressure was 17,510 kPa.

E ;-

J These cuasi-steady pressure measurements are not shown

[

=

'--+--l on the figures.

p

_...]e ;

= I

g

" 4 16.so 17.60 la.4o st:cR::s FIGURE 27 - TEST 917 VALVE STEM PCSITION HISTORY I

(1 in 25.4 m)

I a

i S

o~e

I I

~

g ~

3 S.

-i.-

I I

, [7w 5

i a

=

.._i_

p.

.( y' h

:.

. a. -

i E: YM/4 M k '

4:

~

[

i 1i t

J.V

1. ;

i l

4..

4

{

[.

Q<j.

i l

9 r

2 E3 33 d

e' E

tu I

f is.10 13.20 te.20 is.so 13.10 1a.20 1s.so is.40 FIGURE 30 - TEST 917 SEGMENT 3 FORCE HISTCRY stmas (1 lbf =4.448 N)

FIGURE 33 - TEST 917 STATIC PRE 55URE TAP DTIC RESPONSE m

(1 0s1a=6.894 kPa)

I E

I-e. ".*NqhpA.

CONCLUSICNS

~

The following conclusions were reached in this effort:

(

i 3

- p 1.

These test results provide a data base which B

can be used to benctuark fluid codes to 5.

i Ij.

predict piping nycraulic loads.

i*

3-s

.lb 2.

Cold loop seal designs can have substantially i

g t

tj '

higher loads than steam only designs.

g j3 -' ~ p 3.

Heating

• loop-seal licuid into the range Il'

=

300-350 F can substantially reduce peak is.lo is.ro is.Jo is.so piping loads.

g FIGURE 31 - TEST 917 SEGMENT 4 FORCE HISTORY 4 Accumulated condensate (from 1 eating valves)

(1 lbf=4.448 N) in inadecuately downward sloping discharge lines may produce higher loads chan would be expected from a steam only discharge analysis.

j

,2 l

t l~

ACKNOWLEDGEMENT 5 3

'I

,i The authors ieuld like to thank the staff of l

'3 lt Comoustion Engineering. Windsor. Connecticut, uno j

i. i -

l1

-.j i

J li i

~

~

designed and operated the test facility. Soecial l

thanks go to Mr. 5. Austin for his efforts to modify l

=

g q

i the system structural T.odal.

/

r i

The authors also thank members of the EPRI staf ?

2 I

g j

who participated in the preparation of this paper.

i m

i. 8 i

,l-l 14.1o is.ro is.30 1a.40 stt:m:s FIGURE 32 - TEST 917 STATIC. PRESSURE TAP e

PT09 Resp 0NSE (1 psia =6.894 kPa)

'I 9

l

_y I

,1

~

I II I

I I

.,se, x s

i W

teg er-Ree_ ~_Aput r t57i466 d

l

!I I

I

i i

1

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