Text

Final Rept on Analysis of Prototype PORV Block Valve Steam Blowdown Isolation Qualification Testing for NUREG-0737, Item II.D.1 Issues
	ML20094N443
Person / Time
Site:	Fort Calhoun
Issue date:	04/30/1992
From:	; OMAHA PUBLIC POWER DISTRICT
To:	;
Shared Package
ML20094N438	List: ML20094N435; ML20094N443; ML20094N451; ML20094N455;
References
	RTR-NUREG-0737, RTR-NUREG-737, TASK-2.D.1, TASK-TM NUDOCS 9204060357
	Download: ML20094N443 (137)
	v • d • e

-

i b-OMAHA PUBLIC POWER DISTRICT Final Report on Analysis of Prototype PORV Block Valve Steam Blowdown Isolation Qualification Testing for NUREG-0737,. Item 11.D.1 Issues.

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' TABLE OF. CONTENTS 1.0--

PURPOSE...................................................... 1

-2.0

- BACKGROUND.................................................... 2 3.0 BLOCK VALVE DESIGN BASIS......................................

4 4.0 V ALVE AND ACTU ATOR DE S IGN 0 AT A................................ 6 5.0 VALVE BLOWDOWN TESTING........................................

10 l

5.1-Selection of Test; Vendor.................................

10 1

5.2 Test Loop Configuration..................................

10

- 5.3 Valve and Test Loop Instrumentation......................

11

- 5.4 Blowdown Test Scenarios..................................

11 6.0 STEAM BLOWDOWN TESTING RESULTS................................

13 7.0 DATA' ANALYSIS.................................................

16 7.1 Apparent Valve Factor Determination...................... 16 8.0 APPLICATION OF TEST VALVE RESULTS TO IN-PLANT VALVES..........

17

- 8.1 -Safety function 0peration................................

17

' 8.2~ Determination of Worst Case Valve Factor.................

17 8.3 Required Valve Stem Thrust of In-Plant Valves............18

' 8.4 Evaluation of Previous:MOV Test Data..................... 20-

' 8.5 Comparison of-Test Valve' Motor and Lubrication to In-Plant Valves..........................................

21

9. 0 i CONCL U S I 0N S................................................... 2 5

10.0 REFERENCES

................................................... 26

- APPENDIX--A -- TORQUE-SWITCH AND SPRING PACK CHARACTERISTICS l

' APPENDIX-B -- GENERIC MOTOR PERFORMANCE CURVES FOR 7 FT-LB MOTOR APPENDIX C --' GENERIC MOTOR PERFORMANCE CURVES FOR 10 FT-LB MOTOR APPENDIX D -- DATA PLOTS FOR TEST RUN 1 APPENDIX E--- DATA PLOTS FOR TEST RUN 11-APPENDIX F '-- DATA PLOTS FOR TEST RUN 27 j.

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4 APPEN0lX G----MOTOR. CURRENT TRACES FROM LATEST MOV DIAGNOSTIC 1ESTS APPENDIX-H -- DATA PLOTS FOR TEST RUN 4-APPENDIX 1 -- DATA PLOTS FOR 1EST RUN 6

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APPENDIX J -- DATA PLOTS FOR TEST RUN 8 4

APPENDIX K -- DATA PLOTS'FOR TEST RUN 10 APPENDIX L -- DATA PLOTS FOR TEST RUN 36 APPENDIX M -- STEM THRUST STRAIN GAUGE CAllBRATION CURVE f

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1.0- PURPOSE-1.1 lhe purpose of this report _is to provide the results and subsequent conclusions based upon the analysis of steam

-blowdown data acquired during_open-to-close and close-to-open stroking of a prototype _ test valve.at_Wyle Laboratories from November 21,.1991 through December.17, 1991.

1.2 : An additional-)urpose of this report is to show by. conservative calculations, 3ased.on these test results.that the "as

-installed" configuration of the in-plant PORV block valves is.

adequate to perform their intended safety function as described by the requirements of NUREG-0737, item II.D.1.

1.3 The results and_ conclusions! discussed within this report are

_provided so sufficient-justification is available'to close all-remaining issues' associated-with NUREG-073T, item II.D.1, for the fort Calhoun Nuclear Station.

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2;0'. BACKGROUND-2.1 Requirements for the operation of Power Operated Relief Valve (PORV) Block Valves were discussed in NUREG-0737 ltem II.D.1, paragraph B.

For convenience, this paragraph is stated below:-

" Block Valves--Qualification of PWR block valves q

is..a new requirement.

Since block _vaives must be qualified to' ensure that a stuck-open relief valve can be isolated, thereby terminating a small loss-of-coolant accident due to a stuck-open relief

. valve.

Isolation of a stuck-open power-operated relief valve (PORV) is not required to-ensure safe plant shutdown. 'However,_ isolation capability-under all fluid conditions that could be experienced under operating and accident conditions will result in a-reduction in the number of challenges to the emergency core-cooling system. Repeated unnecessary challenges to these. systems are undesirable."

2.2 In general.the nuclear industry satisfied the above requirements by tasking the Electric Power Research Institute (EPRI) with performing steam blowdown = testing of various' gate valves and motor actuators.

This testing was

_ performed at Dise: Power's Jiarshall Station in 1980.

2.3 The NRC expressed. concern to OPPD that the EPRI steam blowdown testing did not include the same type of gate valves and' actuators that were installed at fort Calhoun Station. Additionally, OPPD did not submit any other full size, full flow test data to demonstrate the operability-of the block valves that would satisfy the NUREG-0737, Item 11.D.1-requirements.

.2.4. Based on these NRC. concerns,-0 PPD _ committed to perform tests of

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an identical (in form, fit and function) PORV block valve.- The NRC staff found this commitment acceptable fer meeting the 11.0.1 requirements to qualify the in-plant PORV block valves by testing.

-2.5--Until a suitable proto+ype valve could be procured and tested, OPPD performed interim measures such as adjusting the torque switches on the actuators to provide the maximum avai able torque from the motors and installir 1ew sr. ring pads to allow the resulting maximum forcs o be applied to the valve stems.. The NRC staff accepted these,nosures for providing i

reasonable assurance of valve operability for the inter' time

. period until? the existing block valves were fully quali.,ed by

_ testing.

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- 2.6 In order to rhow'whether the valve is-qualified.to perform its safety function, the valve must be able to fully close at its worst case design basis conditions with the actuator. torque

- switch set at its expected setting or at the maximum setting

- allowed by actuator or motor limitations (Ref. 10.3).

2.71 To fulfill the above commitment, OPPD purchased ~a prototype test valve, configured a spare SMB-00 motor actuator with the same gear ratio.and spring pack as the installed PORV. block valve actuators, purchased a motor and' contracted with a testing _ facility to perform the necessary steam blowdown tests.

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3.0 01OCK VALVE DE$1GN BASIS 3.1 In order to determine the required test scenario:,

f or operability requirements as stated in NURfG 0737, Jtem 11,0.1, the design basis for operation of the plant's PORV hlock valves needed to be determined.

3.2 Af ter extensive review of all operating and accident conditions, the following fluid conditions were determined to be the worst case design basis conditions-for PORV block valve isolation J

operations as required by_NUREG 0737, item !!.D.1, inadvertent valve mispositioning and subsequent recovery operations were not considered since these were not required by the NUREG.

Max. Upstream-Flin. Downstream Max. Diff.

Max. flow

Temp, fluid.

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2421 15 2406 110,220 660 Steam

= 3. :J lhe steam blowdown isolation design basis conditions are based on closing a PORV block valve for a stuck-open PORV in a,

accordance with Emergency Operating Procedure-00, " Standard Post Trip Actions," at 2350 psia and assuming a 3% ine,trument inaccuraq.

The steam flow is limited by the'oiifice 4ffect of the PORV.

The PORV has a nameplate steam ilow rating of 110,270 lbm/hr saturated steam flow (minimum required of 99,000 lbm/hr) at 2400 psia.

The minimum downstream pressure of 15 asia provides for a maximum differential pressure across (1e block valve and is therefore conservative (Ref. 10.4).

3.5 Potential water and two-phase fluid flow conditions through the PORVs were postulated in Reference 10.5 for a complete loss of feedwater accident, llowever, analysis performed &,

OPPD (i<et.

10.6) showed that the complete loss of feedwater accid w is not a credible accident at fort Calhoun Station.

3.0- lhe NRC also had concerns about water flow conditions tar Jugh the 90RVs fallowing a main feedwater line break at ~ident.

In r

l Reference 10.2, the NRC accepted OPPD's analysis showing that i

the pressurizer does not completely fill with water.

Thus, the L

POP"5 are only required to discharge steam for a feedwater line j

break accident (Ref. 10.2).

3.7 in order to confirm the original sizing of the PORV block valve motor actuators, Crane Valve. Division recalculated the valve stem thrust and torque requirements to operate the Model 797-U valve against 2500 psi differential pressure.

The Crane o

calculation methedology was based upon empirical data and had been used by Crane for over twenty years to size

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operators for gate valves. Using this methodology, Crane

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determined that a thrust of 3653 l!'s would tie required to seat 1

the valve, corresponding to a torque requirement of 57 f'.-lbs.

These values agreed with the original actuator sizing l

calculations (Ref. 10.6).

l 3.8 Subsequent to the EPRI-sponsored Marshall St< am festing results, i

OPPD recalculated the required valve stem thrust using a tuore conservative differential pressure valve disc factor.

This resulted in a new stem thrust requirement of 6812 lbs and 106 ft-lbs of required actuator torque (Ref. 10.6).

These were the interim actuator thrust and torque values that the ins +'lled in-plant actuators were adjusted to (Section 2.5),

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4.0 val VL AND AC10A10R DESl(Ji DAT A 4.1 VALVE DLSIGft 4.1.1 in order to perform the testing, a prototype test volve was procut ed nom CRAtR-ALOYCO, INC., the in-plant PORV i

block valves' c4r 'ginal manuf acturer.

This test vaive was procured under Purchase Order 5061012.

The test vahe was built to the same drawings and bill of materials as the in-plant PORV block valves, including manufacturing tolerances (Ref. 10.7).

4.1.2 Dif f erences between the prototype test valve and the in-plant PORV block valves can be summarized as f ollows:

1 IN PLANT VAlVLS IlSi VAtV[

Packing:

Asbestos Braid Ashestos with inconel Wire Gland Flange:

A351 Grade Cf8M A18? Grade F316 (Casting)

(forging) lionnet Clamp:

A216 WCB A516 Grade 70 (Casting)

(Plate) 4.1.3 Of thn above noted dif f erences, the valve stem pack ing i'.

u the only item t hat caulo pm.sibly af f ect the valve stem thrust by changing the friction loading on the valve stem.

Hewcver, packing f riction is signif icant ly mot e dependent upon the packing gland not torque (i.e., stem packing compression) than on the packing material.

AdditiaTally, the valve stem packing friction load was able to be measured separately from all other valve stem thrust measurements, 50 as not to mask or affett other critical stem thrust measurements.

4.1.4 The in-plant block valves were built to nuclear specifications while the prototype test valve was built to commercial grade specif icat ions with addit ional requirements (RT, Ul, PT, etc.) (Ref. 10.8).

4.1.5 Based on the above, it is OPPD's posit ion that the prototype test valve and the in-plant PORV block valves are identical in f orm, f it and f unction, f igure 4-1 is a drawing of the prototype test valve.

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1 4.2 ACTUATOR Dl:51GN 4.2.1 The tett valve's moter actuator was acquired f rom fort Calhoun Station spare parts inventory.

It was configured l

under Maintenance Work Order 011783 to make the overall actuator ratio and spring pack assembly the same as thost of the installed motor-actuators on the in plant PORV block valves.

A n% motor was alto installed under the same Maintenance Work Order.

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4.2.2 The test valve's actuator torque switch was set at a position of 3.0 in the closing direction and bypassed for 100% of valve stroke in the opening direction.

lhis was done to ensure that.alve characteristics could be monitored without the actuator shutting down during the i

valve stroke, and is consistent with the qualification requirements stated in 5cction 2.6.

i 4.2.2.)

Appendix A 3hons the relationship between the j

torque switch settings, spring pack displacement and actuator output torque.

The accompanying plot is a combination of Limitorque Corporation's spring pack curve for an 0301-111 spring pack (torque switch setting vs. actuator output torque) and til-MOVATS torque switch setting calibration curves for an SMB-00 torque switch.

4.2.2.2 Reference 10.10 confirms the position that actuator output torque can reliably and accurately be determined by knowing the spring pack displacement vs torque relationship.

Thus, torque switch settings are not a_ reliable means of determining actuator torque unless the torque switch is balanced.

4.2.3 The new motor was purchased from limitorque Corporation under Purchase Order C169350.

A 4 ft-lb motor (as installed on the in-plant p0RV block valves) could not be procured.

Therefore, a 10 ft-lb motor was installed on the test valve motor actuator.

Appendix B and Appendix C show the generic motor performance curves for the in-plant installed 7-\\ ft-lb motors and the test valve 10 ft-lb motor.

These curves were produced b, the motor manuf acturers for prototype motors of the same f rame types and sizes.

It is important to note that n_o accurate correlation between the curves can be made.

The motor curves are included in this report only for completeness.

4.2.4 To show that similarity between the test valve motor and i

the installed PORV block valve motors is immaterial.

Appendices D. E and f are provided to show the test valve 7

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and actuator characteristics for open-to-close strokes at ambient conditions with no flow.

These valve strokes are similar to what is done in the plant during actual MOV diagnostic testing._ for the test runs in these appendices, the corrected thrusts at torque switch trip (15T) and the corresponding peak amps are as follows.

lE E RUN CORRfCT(0 THRVE AT IST PEAK AMM 1

7211 lbs

?.72 11 5915 lbs 2.72 27 7428 lbs 2.89 4.2.5 The last MOV diagnostic testing performed during the 1990 refueling outage produced the following results:

VALVE A0JUhif0 1HRUST AT TST

.EAK AMPS p

HCV-150 8700 lbs 1.406 HCV-151 9150 lbs 1.61 4.2.6 -The motor current traces for the above testing are shown in Appendix G.

4.2.7 - Correcting the above n,otor currents for the perf ormance curve voltages and determining the respective motor torque results in:

lEST RUN CORRECTfD AMPS MOTOR TORQUE (ft-lbs) 1 2.83 5 (extrap.)

11 2.83 5 (extrap.)

27 3.08 5.75 (extrap.)

VALVE COR4fCifD AMPS MOTOR 10 ROUE (ft-lbs)

HCV-150 1.53 2.25 HCV-151 1.76 3.0 4.2.8 By comparing t.he above motor current and torque values, it can be determined that no correlation or similarity exists between the 7 ft-lb motors and the 10 ft-lb

-motor.

Examination of the actuator output thrusts (as shown in Sections 4.2.5 and 4.2.6) shows that the in plant-actuators with the 7\\ ft-lb motors appear to be more efficient than the test valve actuator with the 10 ft-lb motor in converting the motor torque to 8

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valve stem thrust.

With actuator output stem thrust being the key parameter in determining the valve and actuatoO output lequirements, motor similarity between the test valve and the in-plant valves is therefore irrelevant.

Differences between the 7 ft-lb motor and the 10 ft-lb motor are justified in Section 8.5 of this report.

4.2.9 A dif ferent stem lubricant was used on the test valve

.than what was used on the in-plant PORY block valves.

lhis was done because new lubricant will be ussed on the in-plant salves beginning with the 1992 refueling outage.

Differences between the stem lubrication are l

discussed in Sect ion 8.5 of this report.

4.3 VALVE AND ACTUA10R DESIGN

SUMMARY

4.3.1 The following is a summary of the_in-plant PORY block valves and actuators as compared to the prototype test valve and actuator.

Valve Tag Number HCV 150/151 Test Valve Valve Manufacturer:

CRANE CRANE Valve Model Number:

797-U 797-U Valve Nominal Size:

2h in.

Valve ANSI Class:

2500#

2500#'

Valve Type:

flex-Wedge Gate flex Wedge Gate Valve Stem Pitch:

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Valve Stem Lead:

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Valve Dwg. Number:

H-30321 CA00691 Valve Spec. Number:-

16.01, Rev. i N/A Actuator Manufacturer:

Limitorque Limitorque Actuator Model-Number SMa 00-74 SMB-00-10 Overall Ratio 46.8 46.8 Spring Pack F/N 0301-111 0301-111 StemLubricant(pre 1992RFO):

Never-Seez NG-165 Mobilux EP-1 Stem Lubricaat spost 1992 Rf0):

Mobilux EP-1 9

5.0 VALVE BLOWDOWN 1ESTING 5.1 Selection of Test Vendor 5.1.1 WnX Laboratories in Norco, California was selected as the tesi facility to perform the blowdown testing under Purchase Order S067874'.

5.? iest Loop Configuration 5.2.1 The flow test loop was configured so pressure losses during steam blewdown conditions could be matched as closely as possible to the expected in-plant steam blowdown conditions.

This was accomplished by evaluating the in-plant FORV piping arrangement from the pressurizer, up to and including the PORVs, and configuring the-flow test facility accordingly.

5.2.2 Afler evaluating the in-plant piping arrangement, the following piping configuration requirements were specified_to and used by the test facility (Rcf. 10.5):

5.2.2.1 Piping upstream of the test valve to the steam and water accumulators shall have an effective resistance coefficient of 4.6.

5.2.2.2 for flow stabilitation and instrumentation considerations, the pipe shall be 2\\ inch, Schedule 160, for at least 10 pipe diameters upstreau. of the test valve.

5.2.2.3 for flow stabilitation and instrumentation considerations, piping downstream of the test valve shall be 24 inch, Schedule 160, 2 feet long.

5.2.2.4 Installation of a PORV or equiulent valve / orifice combination witn a flow area of

.00653 sq. feet (1.094 inches diameter) donnstream of the test valve.

5.2.2.5 Piping downstream of the PORV or valve / orifice combination shall be 4 inch size for a minimum length of 5 pipe diameters.

Beyond this point.

any larger pipe site may be used.

5.2.2.6 The resulting steam and water test loop configurations are shown in figure 5-1.

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p 5.3 Valve and Test Loop lastrumentation 5.3.1 The following is a list of instrumentation utilized in the test loop for measuring valve performance characteristics, tjEASUREMENT RANGE ACCURACY Steam Vessel Pressure 0 - 3000 psig 0

1 3%

Steam Vessel Inventcry DP 0 - 20 psid 10.3%

Flow Venturi Inlet Pressure 0 - 3000 psig 10.3%

flow Venturi Diff. Pressure.

0 30 psid 10.3%

Test Valve Inlet Pressure 0 - 3000 psig 10.3%

Test Valve inlet Temperature 0 - 700 *f 10.5 'f Test Valve Outlet Pressure 0 - 3000 psig 1 35 0

Actuator Motor Voltage 0 - 600 VAC 10.21%

Actuator Motor Current 0 - 20 Amps 12.01%

Valye Stem Position 0 - 15" 10.15%

Valve Stem ihrust 0 - 15,000 lbs 11.5%

Spring Pack Displacement 0 - 1" 10.52%

Actuator Open Limit Switch Open/ ulose Actuator Close Torque Switch Open/Close I

5.3.2 The accuracies. stated above were datermined using the

" square root-sum of the squares' methodology and are conservative.

S.3.3 All data was acquired at a sampling frequency of 1000 HZ.

=

5.3.4 Fluid conditions instrumentation (temperature, pressure, flow, etc.) was installed as shown on figura 5-1.

5.4-Blowdown Test Scenarios 5.4.1 In order to accurately measure valve performance and determine / evaluate for data trends, the following test t

l 11

conditions were established for valve blowdown isolation stroke testing.

TEST VALVE VAtVE MAX. STEAM MEDIA TEMP ('f)

PRESS, (psia) fl0W (Ibm /hr)

Air Ambient 0

None Steam-596 1485 Orifice Controlled Steam 636 1985 Orifice Controlled Steam 653 2235 Orifice Controlled Steam 668 2485 130,000 Air Ambient 0

None 5.4.2 The maximum flow conditions shown above were chosen so as to bound the design basis fluid conditions discussed in Section 3.2.

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i 6.0 STEAM BLOWDOWN TESTING RESULTS P

6.1 Steam blowdown testing was conducted in accordance with the system configuration and steam conditions, with the exception of steam flow, as discussed in previous sections of this report.

Table 6-1 is a summary of the actual stroke testing of the prototype test valve with an overall actuator ratio of 46.8.

6.2 As can be seen by the results listed in table 6-1, the minimum design steam blowdown f104 rate of the PORVs (99,000 lbm/hr) i was exceeded.

Therefore, the steam blowdown flow conditions established during the testing were considered conservative and acceptable. Additionally, the actual maximum line pressure and differential pressure exceeded the worst case design basis values discussed in Section 3.2 of this report.

6.3 In order to determine the test valve's stem thrust measurements at disc wedging conditions during the valve open-to-close stroke, the following conservative method of analysis was utilized for each of the valve open-to-close strokes.

i 6.3.1 The plotted wedging stem thrust (from Appendix H

- through L) was converted to an " apparent" strain.

6.3.2 This " apparent" strain was then corrected for the observed "zero" shift.

This resulted in "true" strain.

6.3.3 The resulting "true" strain was then converted to a "true" load using the strain gauge calibration curve shown in Appendix M.

6.3.4 The wedging load was then determined by subtracting the "true" load from the "zero" load (at "zero" strain as determined by the strain gauge calibration curve),

6.3.5 A load correction was then added to the "true" wedging load.

This load correction was determined by test runs at elevated temperatures and pressures but no differential pressure and flow.

This correction was based upon the expected " running") load (stem rejection load + stem packing friction load and compared to the

" measured" running load.

This load correction was deemed necessary since the tensile load resulting from the elevated stem temperatures appeared to mask the expected compressive running loads.

These load i

L corrections are shown in Table 6-2, 6.3.6 The resulting " actual" wedging loads are shown in Table 6-3.

Additionally, the measured stem position, spring pack displacement and actuator torque _are shown at valve-disc wedging and at torque switch trip.

l 13 l

I 6.3.7 This method of analysis was used since a problem was j

noted during two segments of the original calibration of the stem thrust strain gauge.

This calibration problem resulted ha unrealistic strain-to-thrust conversions which gave very high compressive loads (when plotted).

6.3.7.1 _This calibration problem was most likely due to a cocking of.the valve stem during the initial compressive loading (during calibration), causing stem bending (tensile load) at the strain gauge.

After a 3300 pnund 3

compressive load was applied to the valve

..em, l

t'.e stem became " realigned" and a predictable compressive load curve resulted thereafter.

Appendix M shows the resulting corrected calibration curve f rom.vhich the valve disc wedging loa d and running load corrections were determined.

6.3.7.2 This method of analysis assumes that the strain gauge curve is applicab!c in tensile loading as well as e.mpressive loading.

- 6.4 The'cyclicloadingobservedduringthevalvestrokes(shownin Appendices H through L) were due to a valve stem-to-actuator stem nut misalignment and was noted during all the test runs.

6.5 The actuator's torque switch was unbalanced; that is, the torque switch, while at a setting of 3.0 in the closing direction, tripped-at spring pack-displacements which corresponded to torque switch settings of about 1.5.

This shows that

" torque switch settings" alone cannot determine an actuator's operability.

6.6 The valve was considered fully closed when the vahe disc experienced " disc wedging".

6.6.1

" Disc wedging" is the point where the valve disc is fully inserted (closed)_into the valve seat but has not been

" jammed" or wedged into the seat; This wedging was.

-identified as the instant just prior to the essentially vertical section of the valve stem thrust plot (as shown in Appendices H through L).

6.7 for all valve close-to-open strokes at ambient conditions, valve stem packing friction load was measured by the valve stem thrust strain gauge.

The packing _ friction load varied from 350 pounds

-to 700 pounds.

packing loads used in determining the running i-load correction values and the subsequent valve f actor analysin were' conservatively assumed to be. constant at 350 p)ounds_.(except l_

for Test Run-36 which had a 700 pound packing load.. utilizing l

a low value of stem packing friction load is conservative in that it maximizes the valve disc friction component of the

. measured stem thrust.

14 3

-.= ---

w-.--.--

t i

6.8 An interesting phenomenon observed during the blowdown testing was a reduction in measured valve stem running loads (going from full open to full closed) during steam flow

-conditions.

This phenomenon was also observed during some of the Idaho National Engineering Laboratory (INEL) valve testing and has been explained and understood in the MOV industry as follows:

I 6.8.1. As the valve is going closed and reducing the flow area through the valve bore, the reduction in flow area causes a reduction in pressure below the valve disc (venturi

{

effect).

6.8.2 All through the valve stroke, valve upstream pressure exists in the valve bonnet cavity.

This bonnet cavity pressure is attempting to push the valve stem out of the valve tody.

This is generally referred to as " piston effect" or " stem rejection load." However, this bonnet cavity pressure.is also pushing on the top of the valve dist.

t 6.8.3 When the pressure below the valve disc drops to a certain vaine, the force caused by the dif ferential pressure

-from the top of the valve disc to the bottom of the valve disc overcomes the " stem rejection load" and aids in closing the valve disc.

7 I

i 6

15

.. ~

.. ~. -.

PROTOTYPE BLOCK VALVE TEST RUN

SUMMARY

Test Run Valve Stroke Fluid Max. Temp.

Max. Pressure Max. Ditt. Press.

Max. Flow Stem Stroke Stroke Time Torque Switch No.

(degrees F)

(psig)

(psid)

(Ibmtr) (NOTE 1)

(inches)

(sec)

Setting 1

Open to Close Air Ambient Ambient 0

0 2.81 8.99

<3 2

Cicse to Open Air Ambient Ambient 0

0 2.76 8.73 Bypassed I

3 Open to Close Steam 588 1500 0

0 2.76 8.96

<3 4

Open to Close Steam 606 1508 1493 55,833 2.76 8.96

<3 5

Open to Close Stea m 615 2000 0

0 2.75 9.06

<3

~

6 Open to Close Stea m 642 1944 1938 74,815 2.75 8.94

<3 f

7 Open to Close Steam 571 2264 0

0 2.79 9.04

<3 8

Open to Close Steam 654 2227 2227 86,667 2.76 8.99

<3 I

9 Opsn to Close Stea m 640 2518 0

0 2.75 9.06

<3 I

l 10 Open to Close Steam 563 2518 2518 105,851 2.76 9.01

<3 1

11 _ Open to Close Air Ambient Ambient 0

0 2.75 8.93

<3 12 Close to Open Air Ambient Ambient 0

0 2.75 8.75 Bypassed l

13 Close to Open Steam 600 1537 1537 0

2.77 8.80 Bypessed l

14 Close to Open Steam 600 1682 1682 55,873 2.77 9.04 8ypessed l

15 Close ta Open Steam 642 2100 2160 not avail.

2.81 9.16 Bypassed l

16 Close to Open Steam 613 1938 0

0 2.81 9.08 Bypassed f

17 Close to Open Steam 657 2250 0

0 2.77 9.12 Bypasse 1 (NOTE 2) 27 Open to Close Air Ambient Ambient 0

0 2.83 9.24

>3 28 Close to Open Air -

Ambient Ambient 0

0 2.85 9.00 Bypassed

{

29 Open to Close Steam 560 2209 0

0 2.90 8.97

>3

(

30 Close to Open Steam 569 2250 0

0 2.83 8.91 Bypassed I

1 31 Close to Open Steam 658 2345 2345 73,600 2.84 9.20 Bypessed i

I (NOTE 3)

[

I f

32 Open to Close Air 285 Ambient 0

0 2.80 8.96

>3 33 Close to Open Air 232 Ambient 0

0 2.79 8.71 Bypassed 34 Close to Open Steam 642 2394 2394 105,730 2.83 9.39 Bypessed 35 Close to Open Steam 660 2394 2690 96.190 2.79 9.11 Bypassed 36 Open1o Close Steam.

656 2339 2339 94,286 2.77 8.97

>3 37 Open to Close Water Ambient Ambient 0

0 2.80 8.97

>3 3

~

38 Close to Open Water Ambient Ambient 0

0 2.76 8.86 Bypassed 39 Open to Close Water Ambient 500 0

0 2.81 9.03

>3 a

40 Close to Open Water Ambient 500 0

0 2.75 8.93 Bvpessed i

41 Open to Close Water Ambient 500 500 237,477 (NOTE 4) 2.81 9.04

>3

__ 42 Close to Open Water Ambient 536 536 218.311 (NOTE 4) 2.77 8.93 Bypassed 7

43 Open to Close Water 544 1209 0

0 2.81 9.05

>3 t

44 Close to Open Water 550 1200 264 not avail.

2.82 8.85 Bypassed 45 Open to Close Water 542 1245 1227 224.719 2.86 9.15

>3 TABt.E 6-1 f

PROTOTYPE BLGCK VALVE TEST RUN

SUMMARY

Test Run valve Stroke Fibid Max. Temp. i Max. Pressure Max. Diff. Press.

Max. Flow Stem Stroke Stroke Time Torque Switch No.

(degrees F)

(psig)

(psid)

(!bm/hr) (NOTE y

(~ ches)

(sec)

Setting m

46 Close to Open Water 544 1227 1227 203.947 not avait not avail Bypassed 47 Open to Close Water 525 1500 0

0 2.83 9.03

>3 48 Close to Open Water 546 1513 0

0 not avait not avait Bypassed 49 Open to Close Water 582 1500 1500 228,192 (NOTE 4) 2.80 9.01

>3 50 Close to Open Water 554 1527 1527 222.312 (NOTE 4) 2.77 9.13 Bypassed 51 Open to Close Water Ambient Ambient 0

0 2.78 8.94

>3 52 Close to Open Water Ambient Ambient 0

0 not aveil not avait Bypassed 63 Open to Close Water 542 1598 1598 261.538 2.87 9.19

>3 54 Close to Open Water 542 1600 1600 not avail not avait not avait Bypassed NOTES: 1) A!! flows are steady state values. Some flow peaks were observed but were not considered for analysis.

2) Test Runs 27 inrough 31 were conducted after spring pack and torque switch adjustments.

3) Test Rur.s 32 through 54 were conducted after :he valve was dissassembled for inspechon and reassembled.

4) Flows are corrected for the proper fluid denkity.

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7.0 DATA ANALYSIS 7.1 Apparent talve factor Determination 7.1.1 In order to utilize the test results to confirm the in-plant PDRV block valve operability completely,

" apparent

valve factors were calculated for the test valve at the disc wedging stem position for the various steam blowdown test runs.

7.1.2-These apparent valve factors (AVfs) were determined using the equation below from Reference 10.9, which is derived from the classic form of the industry valve stem thrust equation for gate valves going in the closed direction.

The word "ap'arent* is used because it is assumed the a

valve stem (1 rust not due to valve stem packing friction loads or stem rejection loads is due solely to friction between the valve disc and disc guides / seats, f3-SPL - (P. A )

3 AVf =

0" where: AVf = Apparent Valve factor HeasuredValveStemihrust(lbsl f

3 SPL a Measured Stem Packing friction Load (lbs) 4 1

DP Measured Valvo Dif f erential Pressure (psid)

=

Cross-sectional Area of the volve Stem '(in )

2 A

=

3 P

Measured Test Valve inlet pressure (psig)

=

2 D

Valve Disc Area (in )

A a

7.1.3 Corrected f at " wedging" was taken from Table 6-3, s

while DP and P were taken directly from the plots in Appendices D through 11. A and AD are based upon-valve geometry.3 The valve disc area

-(A ) is based on the mean contact diameter between the D

downstream valve disc and seat.

This diameter was obtained from dimensional inspections at the WYLE test facilities during test valve inspections, for'. convenience and clarification, this measurement location is shown in figure--7-1.-

7.1.4 Table 7-1 shows the results of the determination of AVfs for valve disc wedging for the various open-to-close test runs.

16 0

MPR ASSOCIATEE F-140 9 6( A )

11/09/90

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a DIAMETER USED IN ' _7',

b bi f'FL O W THIS EVALUAT;CN "y' >n"

N,%

TO C ALCULATE I

DISK AREA i

m i. /,! /

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DISK AREAS USED IN THIS EVALUATION Figure 7-1

i i

PORV BtDCA VALVE DATO ANALYS6 M3ULYS

SUMMARY

om. open -veM o-se) r i

VmM.

2 5 ind Rom-Wedge Gsto l

thnut.

CRANE f

l Achetor: tJmstorque SMB4010 I

i i

Downeteam Moon Seat Diameter 2S3 >@es' inree - 5 1996 'sq indes).

I Stem Diameter:

1.125 Indes Wies = 'O9MO eq. hdes) l1 Oscws e<a

[

3638 t>s Test Fbn 4 Stem Thrust pn):

Upeteem Press. Des) 1508 psig j

].

DHt.Freesse psid):

1493 psid i

Stem Peding taed Obs) 350lbs l'

l App. Veh-Factor-0 230{-

i Test Fbn 6 Stem Tivust p):

4693 tas y

l Upsteem Praos. psi) 1944 psig i

U DWL Preenwo paidh 1936 psid f

Stem Peck % toed (bs) 350 t>s

{

i-j l App. Valve Fector:

0239l l.

l Test Fbn 8 Stem Thrust (bs):

5439 bs Upsteem Press. bei)

W psig t

Diff.Pteesmo psidh 2227 psM f

l Stem Pedaing imod (Ibs) 350 t>s l

l

{

lW. Vatw Factor.

02'Sl i

l i

TestIbn 10 Stem Thrust (bs):

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TABLE 7-1 I

t r

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-, -.,,-,,..,m

. ~

8.0 APPLICATION Of-TEST VALVE RESULT 5 TO IN-PLANT VALVES 8.1 Safety function Operation 8.1.1 Because of the qualification requirements of the test valve and the in-plant PORV block valves, the point of

" disc wedging", as determined from the open-to-close valve stroke data during steam blowdown test runs, was considered to be where the valve completely performed its design basis function.

8.1.2 Decause of identical valve designs, this disc wedging valve position is considered to be applicable to the in-plant PORY block valves.

8.1.3_ Therefore, the valve's motor operator must be able to pro.ide enough valve stem thrust to close the valve to the disc _ wedging position for the valve to satisfactorily perform its safety function of isolating steam blowdown f hw.

8.2 Determination of Worst Case Valve factor 5

8.2.1-In order to perform an in-plant PORV block valve operability evaluation, a " worst case" valve stem thrust t

and " apparent" valve factor must be determined.

8.2.2 The strain gauges'used to measure the test valve stem thrust in the closing direction have a total inaccuracy of 1 1.5%.

Applying this inaccuracy to the measured disc wedging valve stem thrust (and subtracting stem packing f riction loads) f rom the 2500 psig steam blowdown test run results in:

Total Stem Thrust X (1.015) - Packing Loads X (.985)

Worst Case Stem Thrust 3791 X (1.015) - 350 X (0.985) 5533 lbs

=

8.2.3 This value of 5533 lbs is the worse case stem thrust

-required above the valve stem packina friction load

}availablethrust)forpropersafetyfunction(isolating steam blowdown flow at 2518 psig/2518 psid) operation of the test valve.

3. 2. :s Pressure and differential pressure measurements have cn

-inaccuracy of 1 0.3% of 3000 psig-(1 9 psig).

In order to maximize the apparent valve _ f ac t or calculatinn, the valve inlet pressure and dif ferential pressure must be minimized.

Thus, at the maximum steam blowdown conditions for disc wedging for the 2500 psig steam l

17

-~~.m_...~....a.,_.-._u.....--.-

blowdown tee; run, the valve inlet pressure and valve differential pressure could have been as low as:

Valve Inlet Pressure:

2518 psig - 9 psig 2509 psig Valve Offferential (2518 psig - 9 psig) -

Pressure:

(0 psig 4 9 psig) - 2518 psig 8.2.4 Utilizing the formula for determining apparent valve factors (Section 7.1.2), applicable test valve geometry parameters, the above worst case valve "available" stem thrust of 5533_lbs, minimized valve inlet pressure and valve differential pressure results in a worst case apparent valve factor of:

f3- (P. A )

3 AVf =

DP. AD where:

AVf = Apparent Valve factor F

= Worst Case Valve Stem Thrust (lbs) 3 OP = Minimized Valve Differential Pressure (psid)

A

= Cross-sectional Area of the Valve Stem (in )

2 3

P = Minimized Test Valve Inlet Pressure (psig) 2 AD = Valve Disc Area (in )-

5533 - (2509 0.994)

(2518). (5.1996) 8.3 Required Valve Stem Thrust-of in-plant Valves 8.3.1 In order to determine the required actuato output stem thrust at the design basis conditions established in Section 3.2, the standard industry valve equation will be combined with a conservative " apparent valve factor" and the standard industry stem packing f riction load of 1500 lbs (for this valve stem size).

l 18

. m

t 8.3.2-The standard valve thrust equation (neglecting stem packing friction load) for valve closing follows :

i I

- (AVf. OPdb. A ) + (Pdb.

A)

D 3

s where: f

-RequiredValveStemThrust(lbs) 3 AVf = Apparent Valve factor DPdb = Design Basis Valve Differential Pressure (psid)

A

= Cross-sectional Area of the Valve Stem (in )

2 3

db = Design Basis Valve Inlet Pressure (psig)

P 2

0 = Valve Disc Area (in )

A 1

8.3.3 Measurements have not been taken on the in-plant PORV_ block valves, but the nominal "mean" seat diameter and valve stem diameter; as acquired f rom the prototype valve dimensional inspections, were utilized in the i

required stem thrust calculation since the test valve was manufactured to the original specifications.

Seat Diameter = 2.573 in.

2 AD = 5.1996 in Stem Diameter = 1.125 in.

2 A3 = 0.994 in t

8.3.4 To account for aging and wear differences between the in-plant valve and the test valve, the apparent valve factor will be increased from 0.232 to a value of 0.3 (29% increase).

This is considered conservative since the in-plant valves have never been operated under a steam blowdown differential' pressure situation and therefore, material wear on the in-plant valves is considered minimal.

Yhis is confirmed by the fact that inspections of the' prototype test valve showed insignificant wear after all testing was completed.

Additionally, the worst case valve factor is already

-based upon steam conditions greater than the design basis conditions.

li L

[

19 1

l l

___ _.. ~ _.._..;__..._

_-,._m

i I

L 8.3.5 Substituting the appropriate values into the above required stem thrust equation results in the following required available stem thrust (above packing load):

I F

= (0.3 2406 5.1996) + (2406 0.994) l 3

F3 6145 lbf 4

8.3.6 This value of 6145 lbs is the valve stem thrust above the stem packina friction load (availabic stem thrust),

required for valve operation at design basis conditions.

8.3.7 When assuming the 1500 lbs stem packing friction load, th' results in a total required stem thrust of 7645 lbs.

8.4 Evaluation of Previous MOV Test Data 8.4.1 To show that an 110V has sufficient capability to operate.

O vdive at the design basis conditions, the total measured valve stem thrust at torque switch trip (151),

o including instrument inaccuracies and " rate-of-loading" effects penalties, must be greater than the valve stem thrust required for the valve to perform its safety function under differential pressure conditions (7645 lbf from Section 8.3.7).

8.4.2 The last MOVtestdatapackages(from1990)forthe in plant PORV block valves were examined and the following vahe thrusts were noted t

VALVE TAG ADJ THRUST AT TST RUNNING LOAD l

HCV-150 8700 lbs 360 lbs HCV-151 9150 lbs 700 lbs 8.4.3 The above running-loads occurred during the entire valve stroke and are due to losses within the actuator, it is not possible to quantify valve stem packing friction l

loads using the ITI-MOVATS test methodology in use at I

fort Calhoun Station. - Therefore, the measured thrust at l

torque switch trip (TST) must be increased (adjusted as L

shown)bystandardindustrypackingloads(1500lbsfor

-this valve stem size).

L 8.-4.4 The test valve exhibited no reduction in thrust output L

at TST under dynamic'(blowdown) test conditions as compared-to static (no-flow) test conditions, if there would be a reduction, it is commonly referred to as a

" rate-of-loading" effect, i

20

l 1

8.4.5 for-the above noted valve stem thrusts, a test equipment inaccuracy of 7.6% was utilized to show a

worst case" stem tbrust measurement.

H.4.6 To determine the value of stem thrust at TS1 considering

" rate-of-loading" effects and test equipment inaccuracies, the following application of these penalties will be utilized:

l Mersured Stem Thrust at 151 - 7.6% - 0% - Packing Loads -

Running Loads Corrected Stem ihrust i

8.4.7 The corrected stem thrusts for the in-plant PORV block valves are as follows:

val)[ TAG CORRfCif 0JifM illRV$1 HCV-150 61,8 lbs HCV-151 6255 lbs 8.4.8 When comparing these corrected valve stem-thrusts to the calculated conservative recuired available stem thrust of 6145 lbs, it is clear-that margin exists at 151 for satisfactory operation of the in-plant PORV block valves

- to isolate steam blowdown flow at design basis i

conditions.

Even though the margin is not excessive, it is considered adequate since the use of 0.3 as the valve factor is based on a 29% increase of the worst case apparent valve factor measured by testing. Additionally, the use of 0.3 as a valve factor is consistent with-industry practice and bounds all steam blowdown l testing results.

8.5 Comparison of Test Valve Motor and' Lubrication to in-plant i

Valves 8.5.1 1here are two differences between the test valve and actuator and the existing in-plant PORV block valves and their actuatort.

8.5.1.1 The test valve had a 10 ft-lb motor installed on its actuator while the existing motors on the

-in-plant PORV block valve actuators are 7\\

ft-lb motors.

8.5.1.2 1he test valve stem lubricant was Mobilux LP-1 grease, while the stem lubricant on the in-plant PORV block valve stems prior to the 1992 refueling outage was Never-Seer NG-165.

Mobilux LP-1 stem lubricant will be used for the 21 r

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8.5.2 1he following analysis was performed to evaluate these-differences.

8.5.2.1 Determining the worst case measured valve stem thrust (from Section 8.2.2) and accounting for i

instrument inaccuracies results in 5533 X 1.015 = 5616 lbs i

8.5.2.2 To calculate the required motor-torque to operate the valve at this stem thrust value, Limitorcue Corporation's siting procedure was utilizec.

8.5.2.2.1 Valve stem thrust is converted to torque by the use of a " stem factor" (SF).

Its application follows:

1 Required Stem Thrust. SF = Required Stem Torqu 8.5.2.2.2 A stem factor of 0.0158 was utilized in the conversion of stem thrust to torque (Ref. 10.19).

8.5.2.2.3 This stem factor value is based on i

no lubrication for a bronze actuator stem nut rotating on a 1.125 inch diameter steel valve stem with a pitch of and a lead of (Ref.

10.19).

i 8.5.2.2.4 Using this stem factor with the required valvo stem threst results in a required actuator stem torque output of:

5616 lbs. 0.0158 88.73 ft-lb 8.5.2.2,5 To calculate the required motor torque for this actuator output stem torque, the following formula was used.

1 Required Motor-Torque =

Reauired Stem Torque (POE) (0,9) (OAR) (DIF) where POE = Pullout Efficiency (0.4 for these actuators) 22

0.9 = Application factor (conservatism used by i

1.imitorque Cor porat ion)

OAR = Overall Actuator Ratio (46.8 for these actuators)

DVf a Degraded Voltage factor (1.0 for these actuators) 8.5.2.2.6 Substituting the appropriate values results in a required motor torque of:

Required Motor Torque

2 y

Required liotor Iorque -

5.27 ft-lbs 8.5.3 When comparing the required motor torque of 5.27 f t-lb to the available motor torque of 7h f t-lb f or the in-plant PORV block valves, it is clear that a 7\\ f t-lb motor would have successfully 0;>erated the test valve.

thus, the use of a 10 ft-lb motor on the test actuator is acceptable and si.uilarity concerns between the 7\\ ft-lb motor and the 10 ft-lb motor are irrelevant as discussed earl (er in Section 4.2.

8.5.4 When performing the above calculation, it is significant to note that the required valve stem torque was determined assuming 20 lubricatico between the actuator stem nut end valve stem.

Thus, the lubrication differences between the test valve and the in-plant PORV blod valves are acceptable since both the Never-Seez and the Mobilux EP-1 do provide same lubrication v,hile the calculation assumes no lubrication.

8.5.5 To ensure the in-plant PORV block valves' actuator motors see sized appropriately, the calculated required valve available stem thrust (6145 lbs) is added to the highest assumed " packing load" (1500 lbs).

This results in a mnimum total required thrust of 7645 lbs.

8.5.5.1 Based upon the last MOV diagnostic test icr the in plant valves, the adjusted thrust (also dcC0unting for test equipment errors) is:

VAlVf TAG ADJUSTfD $ TEM THRUSl HCV-150 8039 lbs HCV-151 8455 lbs 23

y.,.r. _.-_ _

,H, 1

j 8.5.5.2 -Thus, even when correcting for the test equipment accuracies, the installed-in-plant actuaiors are providing.more than the

. conservatively determined required.

-total stem thrust.

This proves that tht i

installed motors are adequately sized, q

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S 9.1 Based ~on the discussion provided in the previous sections of the 1

report, it can therefore be concluded:

9.1.1 The test valve and actuator accurately modeled the in-plant PORV block valves in performance characteristics.

9.1.2 The steam blowdown test conditions exceeded the maximum design basis conditions-for the in-plant PORV block valves and are, therefere, conservative and acceptable.

j 9.1.3 -Based upon~a conservative analysis, the in-plant PORV block valves have margin at actuator torque switch trip to perform their safety' function of isolating steam blowdown flow through a " stuck-open" PORV.

9.2 Based on these conclusions, the in-plant PORV block valves will stroke closed'in'10 seconds (or less) under the maximum expected differential pressure and flow conditions and therefore meet their most severe design basis function.

As a result, all remaining NUREG-0737, item-11.0.1 issues have been addressed by this testing.

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10.0 REFERENCES

10.1 NUREG-0737,.' tem 11.D,1, page II.D.1-1, 3-72 10.2 NRC to OPPD letter of June 25, 1990,

SUBJECT:

Safety Evaluation of i\\dditional Information on NUREG-0737 ltem II.D.1, Puformance Testing of Safety and.'telief Valves, for fort Calhoun Sthtion (IAC No. 44582) 10.3 NRC to OPPD lette of March 4, 1992,

SUBJECT:

Power Operated Relief Valve (POR\\) Block Valve Testing - Fort Calhoun Station, Unit 1 (tic No. M75832) 10.4 ERIN Engineering Ca culatior; C159-90-05.01, " Reactor Coolant System MOVs HCV-150/,51", Revision 0, 9/17/91 (Enclosure for NRCTechnicalReview) 10.5 Combustion Enain % ing Report 602977-MPS-5EFPR-002, " Test Procedure Guideline for Out-of-Plant Testing of the PORV Block Valves at the Fort Calhoun Station," Revision 2 (Enclosure for NRC Technical Review) 10.6 OPPD to NRC letter of June 28, 1988, LIC-88-477,

SUBJECT:

kesponse to Request for Additional Information Concerning NUREG-0737, Item II.D.1 10.7 Telecopy from Bruce Harry (CRANE-ALOYC0, INC.) to Ralph Schwartzbeck (0 PPD) dated 12-10-91,

SUBJECT:

PORV Test Valve, CAI S. O. SJ-212 10.8 CRANE-ALOYCO, INC. to OPPD letter of December 20, 1990,

$UBJECT: OPPD Purchase Order 5061012, CRANE Order #5J-212 10.9

" Review of NRC/INEL Gate Valve Test Program," Electric Power Research Institute, Pre-publication Report NP-7065, Research Project 3433-03, January 1991 10.10 Idaho National Engineerina Laboratory to ITI-MOVATS letter of December 6, 1991,

SUBJECT:

INEL Torque Measurements Position Paper (Draft)-RS-59-91.

10.11 CRANE-ALOYCO, INC. to OPPD letter of September 26. 1991,

SUBJECT:

P.G.. Number 5061012 (CAI SJ-212) 10,12 Progress Report of the Validation Co,nmittee," MOV User's Group, July 1991 10.13 Telecopy from Bruce Harry (CRANE-ALOYCO, INC.) to Ralph Schwartzbeck (OPPD) dated 12-11-90

SUBJECT:

Required Thrust and Torque for 2 " - 2500# Gate-Valve Tag HCV-150 and HCV-151 (SMB-00-7 ), OEM Crane S. O. 868464 (Enclosure for NRC Technical Review) 10.14 Engineering Report 5.0, Rev 3, HENZE-MOVATS Incorporated,

" Equipment Accuracy Summary," October 24, 1991 26

10.15 Limitorque Corporation Selection Procedure, SEL - 1, Page 1 of 1, 5/21/79 10.16 timitorque Corporation Selection Procedure, SEL - 3, Page 3 of 4, 2/26/79 10.17 'Limitorque Corporation Selection Procedure, SEL - 7, 11/79 10.18 WYLE Laboratories Scientific Services and Systems Group, Test Report 57411, Job FS-57411 10.19 Limitorque Corporation Selection Procedure, 900-00003, Sheet 2 of 3, 3/88 10.20 OPPD Internal Memorandum PED-FC-91-305 from R.

L. Phelps to T. J. Mcivor dated January 2, 1991,

Subject:

Degraded Voltage Operation of PORV Block valves HCV-150 and HCV 751 (Enclosure for NRC Technical Review) i-l l

i 27

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P 5

n APPENDIX A TORQUE SWITCH AND SPRING PACK CHARACTERISTICS L

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TORQUE SWITCH SPRING PACK OUTPUT SETTING DISPLACEMENT TORQUE (Inches)

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STEM THRUST-STPAIN GAUGE CAllBRATION CURVE z

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MICROSTRAIN VS COMPRESSIVE LOAD (Actual Test Data) u Compresaivo Microstrain Load (Times 1,000)

(Poundo)

+

48

- 1,000

- 157

- 3,300

- 253

- 4,000

- 320

- 6,000 MICROSTRAIN VS COMPRESSIVE LOAD (Calculated Calibration Curve)

Compressive Load = 13.176u - 1502.2 u

Compressivo Microstrain Load (Times 1,000)

(Pounds) 1,502 0

6,773 400 800

- 12,043

- 1,000

- 14,678

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ML20094N443

Contents

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10.0 REFERENCES

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9.0 CONCLUSION

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ML20094N443

Text

10.0 REFERENCES

SUMMARY

SUMMARY

SUMMARY

SUMMARY

9.0 CONCLUSION

10.0 REFERENCES

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