ML13319B080

Proposed 10 CFR 50.55a Request for Repair of Saltwater Piping Leak (RR-ISI-04-09)

ML13319B080
Person / Time
Site:	Calvert Cliffs
Issue date:	11/14/2013
From:	Dellario D Calvert Cliffs, Constellation Energy Nuclear Group, EDF Group
To:	Document Control Desk, Office of Nuclear Reactor Regulation
References
RR-ISI-04-09
Download: ML13319B080 (51)

Text

Calvert Cliffs Nuclear Power Plant 1650 Calvert Cliffs Parkway Lusby, Maryland 20657 CENG.

a joint venture of CALVERT CLIFFS NUCLEAR POWER PLANT November 14, 2013 U. S. Nuclear Regulatory Commission Washington, DC 20555 ATTENTION:

Document Control Desk

SUBJECT:

Calvert Cliffs Nuclear Power Plant Unit No. 2; Docket No. 50-318 Proposed 10 CFR 50.55a Request for Unit 2 Repair of Saltwater Piping Leak (RR-ISI-04-09)

Pursuant to 10 CFR 50.55a Calvert Cliffs Nuclear Power Plant, LLC, (Calvert Cliffs) hereby requests Nuclear Regulatory Commission approval of the following relief to the requirements of the American Society of Mechanical Engineers Boiler and Pressure Vessel Code, Code Section XI, 2004 Edition, no Addenda.

This 10 CFR 50.55a request for Calvert Cliffs Unit 2 (RR-ISI-04-09) is provided in Attachment (1) and is submitted proposing installation of a mechanical clamping device on a leak discovered on a 12 inch, Code Class 3, Saltwater System pipe.

This 10 CFR 50.55a request, in accordance with Mandatory Appendix IX, Mechanical Clamping Devices for Class 2 and 3 Piping Pressure Boundary, is pursuant to 10 CFR 50.55a(a)(3)(ii) as compliance with all the requirements of American Society of Mechanical Engineers Boiler and Pressure Vessel Code, Code Section XI would pose a hardship without a compensating increase in the level of quality and safety.

This proposed repair is effective for Calvert Cliffs Fourth Ten-Year Inservice Inspection Interval. As required by Mandatory Appendix IX, the mechanical clamping device shall be removed and replaced by a permanent code repair or component replacement at the next scheduled Unit 2 refueling outage which is currently scheduled to begin in February 2015.

Due to the emergent nature of this issue, immediate Nuclear Regulatory Commission review of this 10 CFR 50.55a request is requested.

This letter contains regulatory commitments as listed in Attachment (2).

ANf7

Document Control Desk November 14, 2013 Page 2 Should you have (410) 495-5219.

questions regarding this matter, please contact Mr. Douglas E. Lauver at Very truly yours, Dager.

E De ari Fr Manager - Engineering Services DJD/KLG/bjd Attachments:

(1) 10 CFR 50.55a Request for Calvert Cliffs Unit 2 Repair of Saltwater Piping Leak (RR-ISI-04-09)

Enclosure:

1. Calculation ILD-CALC-0014, Evaluation of 12-LJ-1-2001 Line Enclosure (2)

Regulatory Commitments cc:

N. S. Morgan W. M. Dean, NRC Resident Inspector, NRC S. Gray, DNR

ATTACHMENT (1) 10 CFR 50.55a REQUEST FOR CALVERT CLIFFS UNIT 2 REPAIR OF SALTWATER PIPING LEAK (RR-ISI-04-09)

Calvert Cliffs Nuclear Power Plant, LLC November 14,2013

ATTACHMENT (1) 10 CFR 50.55a REQUEST FOR CALVERT CLIFFS UNIT 2 REPAIR OF SALTWATER PIPING LEAK (RR-ISI-04-09)

RR-ISI-04-09 10 CFR 50.55a Request In Accordance with 10 CFR 50.55a(a)(3)(ii)

--Hardship or Unusual Difficulty Without Compensating Increase in Level of Quality or Safety--

1.

ASME Code Component(s) Affected Calvert Cliffs Unit 2 Saltwater (SW) System pipe line 12"-LJI-201 1. This is a 12 inch schedule STD (12.75 inch OD by 0.375 inch nominal wall) American Society for Testing and Materials A-53 Gr B carbon steel pipe that is rubber lined to prevent interaction of the carbon steel with brackish Chesapeake Bay water. This 12 inch line ties into the 24 inch SW discharge header via a reducing tee. The 24 inch header routes the heat exchanger discharge from both trains of SW to a 30 inch underground pipe and then discharges into the Unit 2 circulating water discharge conduit going back to the Chesapeake Bay.

Design Pressure/Temperature:

50 psig/ 95'F Operating Pressure/Temperature:

35 psig/ 95°F

2.

Applicable Code Edition and Addenda

Calvert Cliffs is currently in its Fourth Ten-Year Inservice Inspection Interval. The Code of Record for this interval is American Society of Mechanical Engineers (ASME) Section Xl, 2004 Edition with no Addenda. The subject piping is ASME Section XI, Class 3. The piping Construction Code is American National Standards Institute B3 1.1, 1967 Edition.

3.

Applicable Code Requirement

The applicable Code requirement from which relief is requested is ASME Code Section XI, 2004 Edition, with no Addenda, Appendix IX, Sub paragraph IX-1000(c)(4) which restricts mechanical clamping devices to nominal pipe size (NPS) 6 when the nominal operating temperature or pressure does not exceed 200'F or 275 psig. This proposed 10 CFR 50.55a request is to allow an ASME Section XI, Appendix IX mechanical clamping device to be installed on this NPS 12 pipe.

4.

Reason for the Request During September 2013, a pin-hole leak was identified on line 12"-LJI-201 1. This condition is currently being addressed by application of approved Code Case N-513-3.

The leak is located approximately five inches downstream of the flange connecting this pipe section to control valve 2-CV-5206.

This valve is located in the SW discharge of Component Cooling Water Heat Exchanger Number 21 and controls the flow through this heat exchanger. The leak is located outside the isolable boundary of a single train of SW. During normal operations SW supports normal heat removal from various plant components and in accident conditions supports emergency decay heat removal functions.

This flaw is in a section of SW piping that cannot be isolated during operation and requires special conditions to be isolated when the unit is off line. As it is impractical to complete a repair or replacement to the SW leak without an extended outage, Calvert Cliffs proposes to use an ASME Section XI, IW A-4130 Alternative Requirement, i.e., a mechanical clamping device described in ASME Section XI, Appendix IX until the next refueling outage, scheduled for February, 2015.

ATTACHMENT (1) 10 CFR 50.55a REQUEST FOR CALVERT CLIFFS UNIT 2 REPAIR OF SALTWATER PIPING LEAK (RR-ISI-04-09)

Appendix IX restricts such devices, under the SW piping conditions, to NPS 6 while the SW piping is NPS 12. All other applicable requirements of Appendix IX will be met.

Flaw Characterization The flaw is located in a section of piping that is directly connected to the common system discharge and cannot be removed from service to gain safe access to the inside for detailed inspection so the root cause cannot be definitively ascertained. Based on ultrasonic testing inspection of the area and the fact that this is an isolated incident, there are two possible root causes for the localized corrosion that resulted in the through wall leak.

A manufacturing defect has resulted in a local failure of the rubber lining, such as a seam split, that has allowed SW to come in contact with the carbon steel.

A flow disturbance from the throttle valve has resulted in localized damage of the rubber liner allowing SW to come in contact with the carbon steel. This cause may also be accelerating the localized corrosion by eroding the passive corrosion layer.

Either of these mechanisms would likely result in the type of failure indicated by the inspections, which appears to be pitting corrosion, a localized form of corrosion where cavities or "holes" are produced in the material.

From nondestructive examination, it appears a portion of the rubber liner is missing at the corroded area indicative of a failure of the liner caused by flow erosion due to some disturbance in the normal flow field at this location.

The area of local wall thinning is oval in shape, with the long axis oriented in the direction of flow and approximately twice the short axis. This shape tends to support a flow assisted mechanism, rather than growth of the corrosion by simple attack of the passive layer.

If the cause for this pitting attack is a flow disturbance, it would be expected that growth of the pit would be strongest in the region most affected by the erosive component of the attack. If a chemical attack of the passive layer is the cause for growth of the pit, then the shape should be non-directional and the pit would be rounded in shape. Since the wall thinning is elongated in shape and growing axially in the flow direction more than circumferentially, this supports the theory that the corrosion mechanism and rate is influenced by a local flow disturbance.

Based on this probable cause, it can be concluded that the pitting corrosion is the result of a local flow disturbance, most likely caused by the upstream flow throttling valve, eroding a local region of the rubber liner, exposing the carbon steel pipe to the corrosive brackish water environment. This corrosive site then led to a through wall condition by continuing corrosion coupled with destruction of the passive layer by the eroding flow disturbance.

2

ATTACHMENT (1) 10 CFR 50.55a REQUEST FOR CALVERT CLIFFS UNIT 2 REPAIR OF SALTWATER PIPING LEAK (RR-ISI-04-09)

FLOW b

6.3" 3.0 Thru wall leaks Ultrasonic examination performed on 10/31/13 Indicates that the through wall dimenson have Increased marginally. There is a third through wall "pin hole" with a 0.06" diameter. Using the center of the largest hole for reference, nominal wall thickness is reached at the following points:

1.2" upstream; 5.1" downstream; 1.6" clockwise; 1.4" counterclockwise (considering flow.) The wear area has elongated In the downstream direction since the last examination on 10/17/13. Area "A" is now 3.5' long by approximately 1" wide.

= Thru Wall

= 0.100" - 0.150"

= 0.150" - 0.240"

= 0.240" - 0.375" Growth Rate Estimation There are four nondestructive examination reports between early September 2013 and late October 2013. These reports corroborate the most likely cause as being flow disturbance related and indicate that the through wall portion of the flaw will continue to grow until it reaches the edge of the flow disturbed region. Growth rate is estimated by comparing data from the earliest (9/6/2013) and latest (10/31/2013) reports. The growth rate is then extrapolated to obtain estimates of the degraded area by February 2015. The axial growth estimate is described here. A similar approach was used for the circumferential estimate.

In the earliest (9/6/2013) report, return to nominal wall thickness was located 1.6 inches upstream and 4.6 inches downstream. In the latest (10/31/2013) report, return to nominal wall thickness was located 1.2 inches upstream and 5.1 inches downstream.

These reports indicate the axial wall thinning is continuing downstream away from the valve and not progressing upstream. The wall thinned region grew in the period between the two reports from 4.6 inches to 5.1 inches or, approximately 0.5 inches in eight weeks. The monthly growth rate for this data, assuming no arrest or slow down, suggests that the flaw would continue to grow at a rate of approximately 0.25 inch axially per month. This is the "High Growth Estimate". It is more likely that the growth will continue at this rate until it is out of the range of the flow disturbance. Then the growth would slow to a much lower rate that is typical for carbon steel in contact with brackish 3

ATTACHMENT (1) 10 CFR 50.55a REQUEST FOR CALVERT CLIFFS UNIT 2 REPAIR OF SALTWATER PIPING LEAK (RR-ISI-04-09) water. We are estimating the growth rate under this scenario at a conservatively high value of 0.15 inch axially per month. This is the "Low Growth Estimate".

A comparison of the two "Growth Estimates" are:

High Growth Estimate Low Growth Estimate

.Direction Axial Circumferential Axial Circumferential Current Length 6.3 inches 3.0 inches 6.3 inches 3.0 inches Rate 0.25 inches 0.5 inches 0.15 inches 0.375 inches Growth Over 4.0 inches 8.0 inches 1.2 inches 6.0 inches 16 Months Total Final 10.3 inches 11.0 inches 7.5 inches 9.0 inches Length Note: The circumferential growth shown in the table is a conservative estimation of the circumferential growth due to the difficulty in measuring the smaller circumferential growth in the presence of the liner.

5.

Proposed Request and Basis for Use Our proposed request is to use an ASME Section XI, Appendix IX, mechanical clamping device until a permanent Repair Replacement can be performed. Design of the mechanical clamping device is shown in calculation ILD-CALC-0014 (Enclosure 1). Upon approval of this proposed 10 CFR 50.55a request, Calvert Cliffs Unit 2 will shift from application of Code Case N-513-3 to the IWA-4133 requirement. The mechanical clamping device will meet all applicable requirements of Appendix IX other than the restriction to NPS 6, including the following:

" All seal clamp components are made from austenitic stainless steel which is acceptable for service from a corrosion standpoint in SW service without any coating and is compatible with the system fluid. External areas of piping that will be in contact with brackish water after installation of the clamp are coated to prevent corrosion.

The clamp design will encompass the projected growth of the flaw as described herein, with additional margin.

No additional supports are required for the mechanical clamping device.

Analysis has shown that the piping is capable of remaining intact with the projected growth of the defect. Additional analysis shows that even in the extremely unlikely event that the defect would grow through wall around the circumference, the existing piping and supports will remain intact and the pipeline ends will move approximately 0.125 inch and will remain within the encapsulation provided by the mechanical clamping device.

The mechanical clamping device has been evaluated for all postulated loads, including seismic Operating Basis Earthquake and Design Basis Earthquake levels, and the stresses remain well below those found in ASME Section XI, Appendix IX, Table IX-3200-1.

The mechanical clamping device is bolted to the piping. Stainless steel tubing acts as sealing O-rings for the mechanical clamping device to maintain a positive seal. No serrated edges are used in the design of the mechanical clamping device.

The piping and supports have been evaluated and determined to acceptably remain below the applicable code allowables for all loading conditions.

4

ATTACHMENT (1) 10 CFR 50.55a REQUEST FOR CALVERT CLIFFS UNIT 2 REPAIR OF SALTWATER PIPING LEAK (RR-ISI-04-09)

The mechanical clamping device is installed in regions of nominal wall thickness away from the local defect, including projected defect growth. Additional margin has been added to the mechanical clamping device size to ensure the defect growth is contained within the mechanical clamping device boundaries.

" The system is a low temperature system and thermal effects are negligible over the length of the mechanical clamping device.

The current and projected defect size has been evaluated as part of the addition of the mechanical clamping device.

Provisions have been made in the mechanical clamping device design and location to ensure that both edges of the mechanical clamping device are accessible for ultrasonic testing wall thickness measurement at least every ninety days. Provisions are in place in the event that the defect monitoring reveals that the defect has grown outside of the mechanical clamping device dimensions.

A leakage monitoring task has been added to facilitate weekly leakage monitoring at the boundary of the mechanical clamping device.

6.

Duration of Proposed Request The mechanical clamping device will remain in place until the next refueling outage scheduled for February 2015 or until Unit 2 enters a shutdown of sufficient duration prior to the refueling outage.

At that time, the mechanical clamping device will be replaced by a permanent code repair or replacement.

5

ENCLOSURE 1 Calculation ILD-CALC-0014, Evaluation of 12-LJ-1-2001 Line Enclosure Calvert Cliffs Nuclear Power Plant, LLC November 14, 2013

r WaLO (W1=A1h0,%

ILD Calculation Cover Sheet Date: 11/11/2013 Calculation No: ILD-CALC-0014 Revision No: 1 Calculation

Title:

Evaluation of 12-LJ-1-2011 Line Enclosure Project Number: 1002-0040 Revision History:

Rev 0: Initial Issue Rev 1: Revised wording to show an allowable torque range and updated Team Clamp Design to Ra iCO C0

'v, 44 Calculation Type: E]

Safety Related El Non-Safety Related Design Verification Required?:

0l No Li Yes (See ILD-EP-0015)

IDV was performed in combination with IDV of CCNPP ECP-13-00947. See ECP-13-00947 for record of IDV.

il/i, /13 Name/Signature Required below.

Charlie Musso Steve Evans Greg Kramer Preparer: Michael Tompkins

_z te:

1V i it/ u

-r

,Page 1

Reviewer: Michael Morgan Date:

Design Verifier: Robert Stakenborghs Date: k k kA Total Number of Pages 40

-Page 1

ILD-CALC-0014 REV 1 Job #1002-0040 ILD-CALC-0014 Rev. 1 November 11, 2013 Evaluation of 12-U-1-2011 Line Enclosure Table of Contents

1.0 Purpose and Scope

3 2.0 Design Input......................................................................................................................................

3 3.0 Assum ptions.....................................................................................................................................

5 4.0 M ethodology and Acceptance Criteria........................................................................................

6 5.0 Docum entation of Com puter Code...........................................................................................

17 6.0 Calculations and Results...........................................................................................................

17 7.0 Conclusion.......................................................................................................................................

22 8.0 References......................................................................................................................................

24 List of Attachments Attachment A: Team Industrial Services Document No. 283380EM ECO A......................................

16 pages Revision History Rev. 0 - Initial Issue.

Rev. 1 - Revised wording to show an allowable torque range and updated Team Clamp Design drawing to Rev A.

Page 2 of 24

ILD-CALC-0014 REV 1 Job #1002-0040

1.0 Purpose and Scope

During the early-September 2013 forced Unit 2 shutdown a pin-hole leak was identified on the Calvert Cliffs Unit 2 Salt Water (SW) pipe line 12"-U1-2011. The SW pipe with the hole is connected to the discharge of Component Cooling Water (CCW) heat exchanger No. 21. In order to mitigate the adverse effects of the hole in the piping, a clamp is being installed to seal the pipe (Ref. 8.5).

This calculation will qualify the vendor clamp design in accordance with the requirements of ASME Section XI Appendix IX. The CCW piping stress is evaluated in ILD-CALC-0013 (Ref. 8.12).

The purpose of this analysis includes:

Induced stress on the clamp due to normal, upset, and faulted loads (i.e. external pressure force induced on the piping due to the installation of the clamp bolting pressure);

Ability of the pipe to maintain its structural design function without failure with the inclusion of the measured flaw; and Analysis of the clamp joints and hardware for normal, upset, and faulted loads to ensure structural integrity for the operating life of this device.

This calculation is safety related.

2.0 Design Input Table 2.1: Design Input Dimension Value Reference Ref. 8.10 Page 82, Ref. 8.4, and 2.1 Pipe outside diameter 12.75 in Ref. 8.11 page B17 Pipe nominal wall 2.2 thickness 0.375 in Ref. 8.11 2.3 Pipe operating pressure 35 psig Ref. 8.9 page 52 2.4 Pipe design pressure 50 psig Ref. 8.9 page 52 Ref.8.10 page 82 & Ref. 8.3 pg 2.5 Pipe material Welded ASTM A-53 gr. B 13 2.6 Pipe allowable stress, Sh 12,700 psi Ref 8.3 page 13 2.7 Clamp inside diameter 14 in Ref. 8.5 2.8 Clamp min. wall thickness 0.375 in Ref. 8.5**

Clamp min. effective 2.9 outside diameter 14.75 in Ref. 8.5**

2.10 Length of clamp 16 in Ref. 8.5 WTOP Pipe Forces (node 290)*: FxWTOp, FyWTOP, Fz 2.11 wrop 467 Ibf, 1101 Ibf, 7 lbf Ref. 8.12 Attachment E page 362 Page 3 of 24

ILD-CALC-0014 REV 1 Job #1002-0040 Dimension Value Reference WTOP Pipe Moments (node 290)*: M2w0op, M, 2.12 wrop, MzWTOP 564 ft-lbf, 16 ft-lbf, 2465 ft-lbf Ref. 8.12 Attachment E page 362 SEISOB Pipe Forces (node 290)*: F.SEISOB, FYSEISOB, Fz 2:13 SEISOB 842 Ibf, 254 Ibf, 143 lbf Ref. 8.12 Attachment E page881 SEISOB Pipe Moments (node 290)*: MxSEISOB, My 2.14 SEISOB, Mz SEISOB 256 ft-lbf, 835 ft-lbf, 459 ft-lbf Ref. 8.12 Attachment E page 881 SEISDB Pipe Forces (node 290)*: FxSEISDB, FySEISDB, Fz 2.13 SEISDB 1462 Ibf, 459 Ibf, 248 Ibf Ref. 8.12 Attachment E page 914 SEISDB Pipe Moments (node 290)*: MxSEISDB, M, 2.14 SEISDB, Mz SEISDB 447 ft-lbf, 1448 ft-lbf, 835 ft-lbf Ref. 8.12 Attachment E page 914 2.15 Clamp material SA 182 GR F 316 Ref. 8.5 Clamp material allowable 2.16 stress (S) 20,000 psi Ref. 8.5 2.17 Stud material SA 193 Gr B8M Class 1 Ref. 8.5 2.18 Stud major diameter 0.625 inches Ref. 8.5 Sheet 1 2.19 Tube seal material Stainless Steel Ref. 8.5 Tube seal outside 2.20 diameter 0.1875 inches Ref. 8.5 2.21 Number of clamp studs 16 Ref. 8.5 2.22 Side bar width 1.0 inches Ref. 8.5 2.23 Seal tube channel width 0.1875 inches Ref. 8.5 Injected sealant channel 2.24 width including wall 0.625 inches Ref. 8.5 2.25 Number of tube seals 4

Ref. 8.5 2.26 Number of injected seals 2

Ref. 8.5 Distance from tube seals 2.27 to sidebar edges 0.09375 inches Ref. 8.5 2.28 Nut factor (K) 0.2 Ref. 8.13 page 3-9 Maximum estimated 2.29 corrosion length 11 in Ref. 8.15 B31.1 Minimum Wall 2.30 Thickness Coefficient, y 0.4 Ref. 8.14 x

y Total DI 1.031 7.75 7.818 Radial Distances from D2 3.094 7.75 8.344 Clamp Centroid to Stud D3 5.156 7.75 9.308 2.31 Centerline D4 7.219 7.75 10.591 Ref.8.5 Modulus of Elasticity of 2.32 stud and clamp 27.7 x 106 psi Ref. 8.5 2.33 Stud Tensile Area 0.226 in2 Ref. 8.16 pg 413 & Ref. 8.5 Page 4 of 24

ILD-CALC-0014 REV 1 Job #1002-0040 Dimension Value Reference 2.34 Allowable Stress of Studs 18,800 psi Ref. 8.5 2.35 Yield Strength of Studs 30,000 psi Ref. 8.14 Manufacturing tolerance 2.36 of pipe wall thickness

+-12.5% of nominal Ref. 8.17 Fastener Length 2.37 (between nuts), It 6.125 in Ref. 8.5 2.38 Stud Hole Diameter, Dbh 0.75 in Ref. 8.5 2.39 Bolting Flange Width 2.8125 in Ref. 8.5 2.40 Washer Thickness 0.5 in Ref. 8.5 Washer Outside 2.41 Diameter 1.0625 in Ref. 8.5 2.42 Nut Head Width 0.9375 in Ref. 8.16 pg. 1055

• Forces and moments are in local coordinates and are the maximum absolute for Node 290. The global coordinates shown in Figure 4.1 correspond to the local coordinates of node 290 in Ref. 8.12 as follows:

X-direction = A-direction, Y-direction = B-direction, and Z-direction = C-direction.

• • The clamp wall thickness is conservatively chosen as the minimum wall thickness between the clamp ID and the bolt holes. Also, adding the wall thickness to the ID in DI 2.7 results in the minimum effective OD in DI 2.9.

3.0 Assumptions 3.1 For purposes of evaluating the clamp stresses, the clamp is assumed to be a circular pipe section with the dimensions listed in design input 2.7-2.10. It is determined from clamp drawings in Ref. 8.5 that no large stress concentrations are present in the clamp design that would make the treatment of the clamp as a circular pipe segment assumption non-conservative. In addition, the small drain hole will be plugged and the size of the hole relative to the clamp wall thickness makes any stress intensification negligible. The wall thickness chosen is based on the minimum wall section of the void portion of the clamp (the minimum wall thickness in design input 2.8 exists between the bolt hole and inner void cavity). This is conservative because the actual clamp design contains much more reinforcing material than is assumed.

3.2 The clamp isn't designed to resist axial loads by friction. It is only considered to resist axial loads for the purposes of conservatism with regard to clamp stress. All loads used for this analysis are assumed in a positive direction and summed in such a manner as to conservatively calculate the largest stress (Ref. 8.1).

3.3 The y and z moments are conservatively summed directly (rather than computing the resultant) in the clamp stress analysis for the purposes of evaluating the peak stress and reaction moments. See section 4.1 for additional details.

3.4 The y and z forces are conservatively summed directly (rather than computing the resultant)in the clamp stress analysis for the purposes of evaluating the peak stresses and reaction moments. See section 4.1 for additional details.

Page 5 of 24

ILD-CALC-0014 REV 1 Job #1002-0040 3.5 The four 3/16" diameter stainless steel tubing seal channels as well as the geometry of the sealant injected between the tubing seals (resulting in 13/16" sealing width per side bar) are credited as the total sealing area of the clamp. Using the sum of the three sealing areas rather than the overall width of each side bar adds conservatism with regards to the total area over which clamping pressure can be applied to the pipe. See section 4.2 for additional details.

3.6 The clamp is assumed to act as a rigid body for the purposes of evaluating the induced clamping pressure on the pipe. This assumption adds conservatism because the maximum allowable deflection of the clamp (0.05 inches per Reference 8.5) is negligible when compared to the overall dimensions of the clamp. See sections 4.2 and 4.5 for additional details.

3.7 The forces and moments computed for the node closest to the clamp (in Ref. 8.12 attachment E) are assumed to be applied at the free end of the clamp (i.e. at the origin in Figure 4.1).

This is conservative because it will develop the maximum stresses in the component.

3.8 Typically the geometrical distribution of stress in a joined member is a frustum of a hollow cone about the stud hole (Ref. 8.16 pg. 428 and 8.13 Section 6.2.5). Due to the complex geometry near the stud holes, the frustum area is conservatively assumed to be the section defined as a hollow cylinder with the 1.5 times the stud hole diameter forming the outer diameter and the stud hole forming the inner diameter. This is conservative because the actual pressure distribution area is larger. A larger pressure distribution area results in a larger member stiffness and therefore a lower maximum stud stress based on Equation 38 of this analysis.

3.9 The clamp material, SA 182 Gr F 316, and stud material, SA 193 Gr B8M, are of similar stainless steel class and have a negligible difference in coefficients of thermal expansion.

Therefore, there will be no excessive stresses between the stud and clamp due to thermal expansion.

3.10 The installed clamp will contact the pipe at areas not affected by the localized corrosion and erosion. Thus, the minimum pipe thickness for the purposes of evaluating clamp-induced pressures is the minimum wall thickness due to manufacturing tolerances (see design input 2.36).

4.0 Methodology and Acceptance Criteria For the purposes of this calculation, the standard coordinate system applied to the analysis herein is as depicted in Figure 4.1 below. This figure also depicts the direction of flow as dictated in Reference 8.4.

Page 6 of 24

ILD-CALC-0014 REV 1 Job #1002-0040 Figure 4.1: Universal Coordinate System and Flow Direction of Pipe with Clamp Installed 4.1 Clamp Stress Methodology The clamp was treated as a hollow, circular beam that was fixed at one end with loads applied to the other to calculate reaction moments. No credit was taken for the pipe structure beneath the clamp, and the clamp is therefore analyzed as absorbing all piping loads.

The moment of inertia, I, was calculated from Ref. 8.1 pg. 974 and substituting design input 2.7 and 2.9. as follows:

2(

4

?

Equation 1 Where r, is the clamp outer radius and ri is the clamp inner radius.

Substituting:

I T ((14.75 in) 4 _ (14 in) 4) = 437.7 in4 The cross sectional area of the clamp is:

A i~rr2 uTr Equation 2 Page 7 of 24

ILD-CALC-0014 REV I Job #1002-0040 A =

(( 14.75 )2 _ (14)2) 16.9 in 2 The stiffness factor, k, is calculated as defined in Ref. 8.1 page 256 for axial-compressive loads on beams (see Assum. 3.2):

k = (I)2 Equation 3 Where F, is the applied load in the global x-direction (axial force) for a given case (WTOP, SEISOB or SEISDB), E is the modulus of elasticity of the clamp, and I is the moment of inertia of the clamp.

The maximum moment is calculated based on Ref. 8.1 pg. 262 (Case 3a) summed with the value for a cantilevered beam with a point load (Ref. 8.1 pg. 208 Case la) with:

Mb =

M0

+ Fri Equation 4 cos(kl)

Where Mb is the resultant moment at the fixed end, Mo is the applied moment (in this case the it is conservatively considered the sum of the applied moment in the global y-direction, M,, and the applied moment in the global z-direction, M,, for the respective load cases considered), I is the length of the clamp, and F, is conservatively considered the sum of the radial forces (the applied load in the global y-direction, Fy, and the applied load in the global z-direction, F, for the respective load cases considered).

The bending stress ( ab) is calculated for each case from (Ref. 8.1 page 158):

Mb

=

ro Equation 5 And normal stress (a,) is calculated for each respective case by (Ref. 8.1 page 141):

yn = L.

Equation 6 A

The shear stress due to torsion (Tt) is calculated by the following (Ref. 8.1 pg. 420). The shear stress due to torsion is calculated for each case:

-t = 2(r-Equation 7 Where M, is the applied moment about the global x-axis. The average transverse shear stress (,r) due to the reaction at the fixed end (Fr ) is given by (Ref. 8.1 pg 158 ) for each case:

Fr Tr =

Equation 8 A

The hoop stress (ah) due to internal pressure is computed from (Ref. 8.1 pg. 608 1b):

Page 8 of 24

ILD-CALC-0014 REV 1 Job #1002-0040 pri ah =

tt Equation 9 Where t is the minimum clamp thickness and p is the internal pressure.

Conservatively, the longitudinal stress (or,) due to internal pressure is given by (Ref. 8.1 pg 609 1c):

pri 2t Equation 10 The total membrane stress is computed conservatively as the summation of all of the average stresses acting across the clamp. For each of the 3 cases evaluated the membrane stresses are:

am normal =

TrWTOP + TtWTOP + a(nWTOP + ah + GI am upset =

Tr SEISOB + Tt SEISOB + an SEISOB + am normal am faulted =

Tr SEISDB + Tt SEISDB + an SEISDB + am normal Equation 11 Equation 12 Equation 13 Similarly the bending stresses are combined as follows:

ab normal = O'b AjrIOP ab upset = ab SEISOB + arb WTOP ab faulted = ab SEISDB + ab WTOP Equation 14 Equation 15 Equation 16 4.2 Pipe External Pressure due to Bolting Methodology The clamp was treated as a rigid body, assuming no gap between the mating flanges of each clamp half, such that the pressure induced on the pipe is due to the torque applied to each of the 16 studs (design input 2.21).

The maximum allowable clamping pressure Pma. (psi) was determined using Equation 17 based on Ref. 8.14 for design of straight piping components.

Px 2SE(tm-A) ax Do-2y(tm-A)

Equation 17 Where SE is the allowable stress in the pipe (psi), tm (in) is the minimum pipe wall thickness due to manufacturing tolerances (Assumption 3.10)), A is the corrosion allowance (0 inches in this case), D, is the outside diameter of the pipe, and y is a temperature and material-dependent correction factor (design input 2.30). The allowable stress considered in Equation 17 does not account for seismic loading scenarios of the pipe, due to the fact that this induced pressure is highly localized rather than a global external pressure.

The effective sealing width of each 1 inch sidebar (design input 2.22) is computed by the summation of the width of two of the stainless steel tubing seals (design input 2.20), the Page 9 of 24

ILD-CALC-0014 REV 1 Job #1002-0040 width of the injected sealant cavity (design input 2.24) and the void area between the walls of the sealant cavity and the inside width between the two tubes, as shown in Figure 4.2.1 below.

Figure 4.2.1: Seal Channel Geometry To determine the overall clamp sealing width, the sum of the sealing width of each of the two sidebars (ref. 8.5) was computed. This width was then used to compute the overall sealing area of the clamp on the pipe using Equation 18 below:

Aseal -' iiDoLseal Equation 18 Where D, is the outer diameter of the pipe (in), and Lseal is the overall clamp sealing width (in).

The total stud clamping force, Fstud (Ibf), may be computed using the following relation of known parameters:

Fstud = AsealPclamp Equation 19 Note that this force is determined from the maximum allowable pressure force (Pmax above) that can be exerted on the pipe. This pressure is modified to a lower value (Pciamp) to reflect a 3% margin for conservatism in practice.

The above value of Fstud is then used to determine the maximum allowable preload force that can be exerted on the clamp by each stud, Fi, by the equation below:

Page 10 of 24

ILD-CALC-0014 REV 1 Job #1002-0040 F; = Fstud Equation 20 N

Where N is the number of studs installed on the clamp housing.

The required stud nut torque T (in-lb) to achieve the maximum allowable preload, Fi, as determined above is then computed using the following equation from Reference 8.13page 3-3:

T = KdstudFi Equation 21 Where K is the nut factor (design input 2.28), and dtUd is nominal stud diameter (in).

4.3 Structural Evaluation of Pipe Wall with Flaw The structural adequacy of the pipe containing the through-wall leak was evaluated at an eroded condition using the ASME B31.1 methodology for evaluating the need for reinforcement of branch connections due to internal pressure for a given branch hole size.

The need for reinforcement material is determined to ensure that the pipe has sufficient structural strength after the branch is added. If the pipe wall is thick enough to ensure structural adequacy for the size branch hole, then no further reinforcement is required. In this case, the material (pipe wall) remaining around the eroded area must be thick enough to provide the required reinforcement for a hole which encompasses the largest expected eroded hole size, based on flaw growth.

The most severe estimate for erosion is used to evaluate an encompassing branch hole size.

From 2.29, the largest eroded length is 11". Therefore, an 11" diameter branch hole size will be used to estimate the required reinforcement area from the surrounding pipe.

The minimum required thickness of 12"-U1-2011 salt water pipe (at un-eroded condition) is first determined by Eq. 22 below.

tmh =

P-Doh Equation 22 2*(SE+P-y)

Where th is the minimum wall thickness required to withstand the internal pressure (in), P is the design pressure of the 12"-U1-2011 salt water pipe (psi), Doh is the outer diameter (in), SE is the maximum allowable stress in the material due to internal pressure (psi), and y is a temperature and material dependent coefficient.

The area required to reinforce a branch hole, A7, can be calculated by Equation 23.

A7 = tm

• Equation 23 Where dl is the inside centerline longitudinal dimension of the finished branch opening in the run of pipe (in).

Page 11 of 24

ILD-CALC-0014 REV 1 Job #1002-0040 The inside centerline longitudinal dimension, dl, used in Eq. 23 is calculated with Eq. 24.

d, = Dob -

2

• Tb Equation 24 Where Dob is the outer diameter of the branch connection (the 11" diameter eroded section), and Tb is the branch connection thickness which is zero since the postulated branch is being evaluated as a hole.

The area provided by excess pipe material, A,, is calculated from Equation 25.

A, = (2

• d2 - dl) * (Th - tin)

Equation 25 Where Th is the actual thickness of the pipe (which conservatively accounts for a 12.5%

manufacturing tolerances) and d 2 is the half width of the reinforcing zone and is calculated from Equation 26.

d2= min (max (d,, Tb + Th +-

, Doh)

Equation 26 4.4 Fastener Analysis 4.4.1 Joint Stiffness The fastened section of the clamp required inspection to determine the force distribution between the stud and the member.

The stiffness constant factor provides the relationship between the force applied to the joint and the force applied to the stud. This relationship is given in Equation 27 (Ref. 8.16 pg 436)

C =

km Equation 27 kf+km Where C is the stiffness constant of the joint, kf is the fastener stiffness and km is the stiffness of the member.

The fastener, in this case the stud, stiffness is calculated using Equation 28 (Ref. 8.16 pg. 427).

kr = At!E Equation 28 It Where At is the tensile area, E is the modulus of elasticity of the material, and It is the threaded length of the stud between the nuts, which includes any thickness added by washers (Design Input 2.37).

Under normal circumstances the member stiffness is determined using a conical frustum centered about the stud hole that encompass the area that absorbs the stud Page 12 of 24

ILD-CALC-0014 REV 1 Job #1002-0040 load. However, due to the shape of the clamp, the use of a conical frustum would encompass areas beyond the clamp's dimensions. Therefore, the area of pressure distribution is reduced to a hollow cylindrical area surrounding the stud hole (see Assum. 3.8). Since only one washer is used per stud, each member stiffness will be calculated differently due to their differing pressure distribution areas and lengths.

The pressure-distribution area (Ap) is defined as the area encompassed by either the washer outside diameter or the nut head width (Dbo) minus the stud hole diameter (Dbh) (Ref. 8.16 pg. 431):

A Dp

=

4 7t

°b 4h Equation 29 4

4 The member stiffness (km) is given by Equation 28, except A is substituted with the pressure-retaining area (Equation 29), and I is the length of one member, either the length of the bolting flange and the washer thickness or just the length of the bolting flange.

The member stiffnesses are summed by the following equation (Ref. 8.16 pg. 427).

1 1

1

-- = 1+ I Equation 30 k k k,

Where k, is calculated using the washer outside diameter and includes the washer thickness, and k2 is calculated using the nut head width and only the bolting flange length. The washer may be simply added to the thickness of a member due to the fact that their pressure distribution areas and moduli of elasticity are identical.

With the combined member stiffness and the fastener stiffness calculated, the stiffness constant of the joint may be calculated using Equation 27.

The loads applied to the joint may now be calculated and broken into forces applied to the stud.

4.4.2 Stud Loading In order to conservatively calculate the applied stud load, the clamp was treated as a rigid member (Assumption 3.6). Tensile and shear stresses were accounted for when determining the applied stud load in the normal, upset, and faulted cases. The forces and moments are assumed to be acting about a coordinate system located at the centroid of the clamp, but identical in global orientation to that shown in Figure 4.1.

Four tensile forces acted on the clamp stud. The first of which was a moment about the axial direction, Ma. Since the axial moment acts equidistant to all studs, it was divided by the distance from the x-axis to the stud centerline and the total number of joints in order to obtain a tensile force per joint. This is illustrated in Equation 31.

Page 13 of 24

ILD-CALC-0014 REV 1 Job #1002-0040 F

Equation 31 z'N Where Ma is the axial moment, z is the z-distance from the moment axis to the stud centerline, and N is the total number of joints The pressure acting on the inner surface area of the clamp also contributes to the tension in the studs. This force acts equally on all studs as well, and was therefore calculated using Equation 32.

F = P-2nrI Equation 32 N

Where r is the inner radius of the clamp, I is the length of the clamp void that sees the piping pressure, and P is the internal design pressure.

The third tensile force acting on the studs is induced by the moment about the z-axis (assumed to be translated to the center of the clamp in Figure 4.1). This moment does not act equally on all studs but does act equally on the four sets of studs located at four distinct distances from the moment axis.

Equations 33, 34, 35, and 36 (Ref.

8.16 pg. 456) relate the moment to the four distances and four forces at their respective distances.

M = 4F 1x, + 4F 2x 2 + 4F3x 3 + 4F4x 4 Equation 33 FL = x*

Equation 34 F 2 x2 I=

Equation 35 F 3 x 3 L = x*

Equation 36 F 4 x 4 Where M is the moment, x1, x2, x3, and x4 are the various distances to the stud centerlines from the moment axis, and F1, F2, F3, and F4 are the associated forces acting on the stud centerlines. Each force is multiplied by 4 to account for the four studs at the same distance from the moment axis. Distances are arranged such that distance x, is the shortest distance from the moment axis to stud centerline and distance x4 is the greatest distance (see design input 2.31). Equations 33, 34, 35, and 36 can be combined to solve for F4 as shown in Equation 37.

Mx 4 F4 = 4(X2+xz2+x32+x2)

Equation 37 Solving for F4 returns the largest force induced by M on a joint and, for conservatism, was used in calculating the applied load for all 16 joints.

The final force adding tension to the studs was induced by Fy, which imposes equal but opposite forces in the y-direction on the two ends of the clamp. This creates a Page 14 of 24

ILD-CALC-0014 REV 1 Job #1002-0040 moment about the z-axis equal to the product of F, and the total length of the clamp, L (Equation 38). With this moment applied about the centroid, the forces may be determined using Equation 37 and appropriate distances from the moment axis to the stud centerline.

M = FY *L Equation 38 The magnitude of the four tensile forces were then summed into a single force which is the total force applied per joint. The applied force per joint is then multiplied by the stiffness constant factor to determine the force applied to the stud.

This is shown in Equation 39 Pb = CP Equation 39 Where Pb is the portion of the external tensile load taken by the stud and P is the external tensile load applied to the joint. The preload is then added to the force applied to the stud to determine the normal load case force on the stud. The tensile stress per stud is then calculated by dividing the normal load case force by the stud tensile area, which is.226 in2 (Design Input 2.33).

Shear forces were also considered when determining the applied stud load. Two shear forces were inspected while determining the stud stress.

The first shear force was caused by a force in the z-direction, F, acting on opposite ends of the clamp with equal and opposite forces, creating a moment on the clamp equal to F, multiplied by the total length of the clamp. The induced moment acts about the y-axis at the centroid and therefore does not act equally on all studs but does act on the four distinct stud distances from the centroid of the clamp. Equation 37 is again used to determine the resulting force at distance 4.

Due to the orientation of the moment axis and the stud centerline, radial distances were used to calculate the force on each stud. This required the square root of the sum of the squares of the x and y distances (SRSS) to determine the appropriate distance from stud centerline to moment axis.

The moment about the y-axis, My, also contributed to the shear force in the studs.

The force per stud created by this moment is not equal from stud to stud. For this reason, Equation 37 is used, again with radial distances, to determine the greatest resulting force per stud.

These two shear forces were then added to determine the total shear force per stud.

The shear force per stud was then divided by the bolt area (Design Input 2.33) to determine the shear stress caused by the two.shear forces. The sum of the tensile and shear stresses was then taken to calculate the total stud stress. Stresses for normal, upset, and faulted cases may then be evaluated, using Equations 40, 41, and 42 (Ref. 8.14), and compared to the stud's allowable stress (Design Input 2.34).

Page 15 of 24

ILD-CALC-0014 REV 1 Job #1002-0040 Normal = SWTOP Equation 40 Upset = SWTOP + SSESIOB Equation 41 Faulted = SwroP + SSEISDB Equation 42 Where S is the calculated stress for the respective load case. In addition to ensuring the allowable stresses are not exceeded, the nut must also lock into place on the stud. In order for this to occur, the stress induced by the preload must exceed 20%

of the stud's yield strength (Ref. 8.13).

4.5 Acceptance Criteria 4.5.1 Clamp Stress The results of the clamp stress analysis are considered acceptable if it is shown that the clamp stress is less than the allowable stress in accordance with Ref. 8.2. The clamp stress allowables are as follows:

Table 4 ASME Table IX-3200-1 Stress Limits For Design and Service Loadings (Ref. 8.2)

Service Limits Stress Limits (1)

Design and Level A (Normal) am < 1.0 S

-am + OU < 1.5 S Level B (Upset) am < 1.1 S a,, + ah < 1.65 S Level D (Faulted) aUm < 2.0 S I

Uam +ah < 2.4S Notes:

(1)

The symbols used in Table 4-1 are defined as follows:

ar = membrane stress ab = bending stress S = allowable stress= 20,000 psi for the clamp material (design input 2.16) 4.5.2 Pipe External Pressure due to Bolting The pressure induced on the piping by the clamp is considered acceptable if the pressure does not exceed the maximum allowable pressure as calculated using methodology presented in Reference 8.14, i.e. Pciamp< Pmax.

4.5.3 Structural Evaluation of Pipe Wall with Flaw The eroded defect hole size (evaluated as a branch opening) is considered acceptable if the area provided by excess 12"-U1-2011 pipe material is greater the required reinforcing area i.e. A, > A7.

Page 16 of 24

ILD-CALC-0014 REV I Job #1002-0040 4.5.4 Fastener Analysis The stud stress is considered acceptable if the stud stress in the faulted case is less than the stud's allowable stress for normal conditions, which is 18,800 psi (Design Input 2.34).

The stud preload is considered acceptable if the preload exceeds the force applied to the stud.

Stud Preload > Stud Applied Load The nut locking is considered to be acceptable as long as the preload induced stress exceeds 20% of the stud's yield strength (Ref. 8.13), or 30,000 psi (Design Input 2.35).

5.0 Documentation of Computer Code Not applicable.

6.0 Calculations and Results 6.1 Clamp Stress The results of Substituting the relevant design input into Equations 1 through 10 is shown in Table 6-1.

Table 6-1 Summary of Stress Results WTOP SEISOB SEISDB Bending moment (Mb) in*lbf 47,500 21,880 38,708 Equation 4 Bending stress (Ob ) psi 800 369 652 Equation 5 Normal stress (an) psi 28 50 86 Equation 6 Shear stress due to torsion (rt) psi 57 26 45 Equation 7 Shear stress due to reaction (r,) psi 65 23 42 Equation 8 Hoop stress (ah) psi 933 N/A N/A Equation 9 Longitudinal stress (or,)

467 N/A N/A Equation 11 Substituting into Equation 11 with results from Table 4-1:

amnormal = 65 psi + 57 psi + 28 psi + 933 psi + 467 psi = 1,550 psi Page 17 of 24

ILD-CALC-0014 REV 1 Job #1002-0040 Substituting into equation 12 from the results in Table 4-1:

am upset = 50 psi + 26 psi + 23 psi + 1,550 psi = 1,649 psi Substituting into equation 13 from the results in Table 4-1 am faulted = 42 psi + 45 psi + 86 psi + 1,550 psi = 1, 723 psi Substituting into Equations 14 through 16 results in:

ab normal = 800 psi ob upset = 1,169 psi ab faulted = 1,452 psi Equations 11 through 13 are then summed with the bending loads (Equations 14 through

16) for each case in accordance with Ref. 8.2.

Normal: amnormal + abnormal = 1,550 psi + 800 psi = 2,350 psi Equation 40 Equation 41 Upset: am upset + ab upset =

= 1,649 psi + 1,169 psi = 2,818 psi Faulted: am faulted + ab faulted Equation 42

= 1,723 psi + 1,453 psi = 3, 176 psi All forces are less than the allowables as shown in Table 6-2 and are therefore acceptable.

Also note that the low stress ensures that margin would be maintained after any stress intensification factors were applied due to the drain hole or other slight deviations from the circular geometry. This therefore reaffirms Assumption 3.1.

Table 6-2: Clamp Design & Service Loading Stress Summary Stress (psi)

Allowable (psi)

Normal am normal 1,550 20,000 am normal + ab normal 2,350 30,000 Upset am upset 1,649 22,000 am upset + ab upset 2,818 33,000 Faulted am faulted 1,723 40,000

_m faulted + ab faulted 3,175 48,000 Page 18 of 24

ILD-CALC-0014 REV 1 Job #1002-0040 6.2 Pipe External Pressure due to Bolting The maximum allowable clamping pressure is calculated via the substitution of applicable design input values into Equation 17.

2(12,700)0.328 P.na =

-= 667 psi 12.75 - 2(0.4)0.328 As noted in section 4.2, the maximum allowable clamping stress was subject to a correction factor of 3% in effort to provide a safety margin against over-tightening of the clamp studs.

Pciamp = 0.97(Pmax) = 650 psi Equation 43 The effective sealing width of the clamp was computed by subtracting the total width of the stainless steel tubing seals and injected sealant void from the overall side bar width in accordance with design inputs 2.20, 2.22, and 2.24.

Lseal = 2 2 *

+

= 1.625 inches Equation 44 The overall sealing area of the clamp was computed in accordance with Equation 18 and design input 2.1 and the results of Equation 44.

Aseal = IT(12.75)1.625 = 65.090 in 2 Equation 19 was implemented to determine the total stud clamping force using the total sealing area and the results of Equation 43.

Fbaot = 65.090(650) = 42,308 lbf The maximum allowable preload force due to each stud is then calculated using Equation 20 and design input 2.21.

42,308_

Fi =

162,30 = 2,644.3 lbf The required stud torque is correlated to the maximum allowable preload on each stud by Equation 21. Design input relevant to Equation 21 include design inputs 2.18 and 2.28.

T = (.2(0.625)2644.3)/12 = 27.5 ft - lbs From the results obtained from Equation 21, a maximum of 27.5 ft-lbs of torque can be applied to each of the 16 clamp studs without risk of compromising the structural integrity of the pipe. Due to the fact that this torque was calculated with a corrected pressure (Pciamp),

the acceptance criteria of Pcarmp < Pmax is met.

Page 19 of 24

ILD-CALC-0014 REV 1 Job #1002-0040 6.3 Structural Evaluation of Pipe Wall with Flaw The minimum wall thickness in the pipe is calculated to be 0.025" from Eq. 22.

50psi

• 12.75in

= 2 * (12,700psi + 50psi

• 0.4)

The required reinforcement area is calculated to be 0.276 in2 from Eq. 23.

A 7 =.025in

• 11in = 0.276 in 2 The excess area provided by 12" saltwater pipe is calculated below from Eq. 25.

A. = (2

• llin - llin) * (0.328in -. 025in) = 3.33in 2 6.4 Fastener Analysis The results of substituting the relevant design input into Equations 27 through 29 are shown in the table below.

Table 6.4: Summary of Stiffness Calculations Fastener Stiffness kf=1.02e6 lbf/in Equation 28 Stiffness Area of Member 1 (w/washer)

Ap1=.445 in2 Equation 29 Stiffness Area of Member 2 (w/ nut head)

Ap2=.249 in2 Equation 29 Stiffness of Member I (w/ washer) kl=3.72e6 lbf/in Equation 28 Stiffness of Member 2 (w/ nut head) k2=2.44e6 lbf/in Equation 28 Total Member Stiffn'ess km=1.47e6 lbf/in Equation 30 Stiffness Constant of Joint C=0.409 Equation 27 The results of substituting the relevant design input into Equations 28 through 38 are shown in Table 6.5.

Table 6.5: Summary of Tensile Forces on Joints All values per stud unless noted Equation WTOP SEISOB SEISDB Total Moment from by F, (ft*lbf) 38 1468 339 612 Tension from Moment created by Fy(lbf) 37 356 82 148 Tension from Ma(Ibf) 31 55 25 43 Tension from M, at Greatest Dist. (Ibf) 37 598 111 202 Tension from Internal Pressure (Ibf) 32 1924 N/A N/A Total Tensile Force (Ibf)

Summed 2932 218 394 Page 20 of 24

ILD-CALC-0014 REV I Job #1002-0040 Table 6.6: Summary of Shear Forces on Joints All values per stud unless noted Equation WTOP SEISOB SEISDB Total Moment from F, (ft*lbf) 38 9

191 331 Shear from Moment from F, (lbf) 37 0.9 18 32 Shear from M. at Great Distance (lbf) 37 1.5 80 140 Total Shear Force [SF] (lbf)

Summed 2.4 99 171 Table 6.7: Summary of Stud Analysis All values per stud unless noted Equation WTOP SEISOB SEISDB Equivalent Applied Tensile Load [T] (lbf) 39 1200 89 161 Tensile Load Plus Preload [FN] (lbf) 38 3844 N/A N/A Tensile Stress in Stud [o] (psi)

FN/A 17008 395 713 Shear Stress in Stud [T] (psi)

SF/A 11 438 759 Summed Tensile & Shear Stresses [S]

T+o 17019 832 1472 (psi)

Design and Service Loading Stud Loads without Preload Normal = TWTOP = 1200 lbf Upset = TWTOP + TSEISOB = 1289 lbf Faulted = TWTOP + TSEISDB = 1361 lbf Design and Service Loading Stud Loads with Preload Normal = FN + TWTOP = 3844 lbf Upset = FN + TWTOP + TsEIsoB = 3933 lbf Faulted = FN + TWTOP + TSEISDB = 4005 lbf Page 21 of 24

ILD-CALC-0014 REV 1 Job #1002-0040 Design and Service Loading Stud Stresses Normal = SWTOP = 17019 psi Upset = SWTOP + SsEISOB = 17852 psi Faulted = SWTOP + SSEISDB = 18491 psi 7.0 Conclusion 7.1 Clamp stress All combined stresses are less than the allowables in accordance with Ref. 8.2. Therefore, the clamp seal stress is acceptable.

Table 7-1: Design and Service Loading Stress Summary Stress (psi)

Allowable (psi)

Normal Cm normal 1,550 20,000 Cm normal + Ub normal 2,350 30,000 Upset 6 m upset 1,649 22,000 6m upset + Gb upset 2,818 33,000 Faulted 6m faulted 1,723 40,000 7

1 1m faulted + 6b faulted 3,175 48;000 7.2 Pipe External Pressure due to Bolting As evidenced within Section 6.2, the computation of the maximum allowable bolt torque.is computed such that the pressure induced on the pipe by the clamp (P1iamp) will not exceed the maximum allowable applied pressure (Pmax). Thus, the acceptance criteria of PcIamp < Pmax is satisfied. Table 7-2 below tabulates the results of the calculations performed pursuant to sections 4.2 and 6.2.

Page 22 of 24

ILD-CALC-0014 REV 1 Job #1002-0040 Table 7-2: Pipe External Pressure due to Bolting Summary Maximum Allowable Clamping Pressure (Pmax) psi 667 Equation 17 Corrected Allowable Clamping Pressure (Pciamp) psi 650 Equation 43 Overall Clamp Sealing Area (Aseal) in 2 65.090 Equation 18 Total Stud Clamping Force (Fbolt) lbf 42,308 Equation 19 Max. Allowable Preload per Stud (FI) lbf 2644.3 Equation 20 Max. Allowable Stud Torque (T) ft-lb 27 Equation 21 The stud torque calculated in Table 7-2 is the maximum allowable torque that can be applied to the clamp nuts such that the pressure induced on the pipe by the clamp does not exceed 650 psi as computed by Equation 43. Thus, 27 ft lbs is the maximum allowable Upper limit for bolt torque.

7.3 Structural Evaluation of Pipe Wall with Flaw The required reinforcing area, A7 = 0.276in 2, is less than the reinforcing area provided by excess pipe material, A1 = 3.33in 2. The results of this analysis show that the piping integrity may be maintained without the addition of the pipe clamp (reinforcement). Therefore, a defect whose size is bounded by a 11" diameter circle is acceptable per the methodology of Ref. 8.14.

7.4 Fastener Loading The Stud Stress is considered acceptable because the stud stress in the faulted case is less than the stud's allowable stress for normal loads.

Faulted Case: 18,491 psi < Bolt Allowable: 18,800 psi The stud preload is considered acceptable because the preload exceeds the expected faulted applied load (WTOP Applied Tensile Load plus SEISDB) accepted by the studs.

Stud Preload: 2644 lbf > Stud Applied Load: 1361 lbf Due to the fact that the stress induced by the preload of 2644 lbf/0.226 in2 = 11,699 psi is greater than 20% of the stud's yield strength (0.2 x 30,000 psi = 6,000), the nut can act as a locking device.

The stud preload stress and nut locking forces have sufficient margin such that a torque range of 23 ft lbs to 27 ft lbs is acceptable. The torque range is necessary to account for torque wrench accuracy.

Page 23 of 24

ILD-CALC-0014 REV 1 Job #1002-0040 8.0 References 8.1 Roark's Formulas for Stress and Strain, Eighth Edition 8.2 2004 ASME SECTION Xl Appendix 9 8.3 CCNPP Calculation M-93-038 Rev. 1, "Component Cooling Pump Room Piping - Unit 2" 8.4 CCNPP Drawing 91374 Sheet 1 Rev. 18, "Component Cooling Water Pump Room Piping -

Salt Water Cooling System - Unit 2" 8.5 Team industrial Services Document No. 283380EM ECO Rev. A (Included as Attachment A) 8.6 Calvert Cliffs Engineering Standard ES-040 Rev. 00, "Piping Design Criteria" 8.7 CCNPP Calculation CA00700 Rev. 0, "Modification to Pipe Supports Associated with Salt Water Piping System" 8.8 CCNPP Calculation CA00702 Rev. 0, "Evaluation of Pipe Supports for Salt Water Piping System due to Minor Deviation from Design Condition and/or Proximity to Adjacent Anchor Bolts" 8.9 Calvert Cliffs M-601 Piping Class Summary Sheets Rev. 49 8.10 Calvert Cliffs M-600 Piping Class Sheets Rev. 76 8.11 Crane Technical Paper No. 410, "Flow of Fluids Through Valves, Fittings, and Pipe,"

Reprinted 2006 8.12 ILD-CALC-0013 Rev. 0, "Impact -of Pipe Clamp on Calvert Cliffs Nuclear Power Plant Component Cooling Water Piping Stress" 8.13 EPRI-TR-104213, "Bolted Joint Maintenance and Applications Guide", Published December 1995 8.14 ASME B31.1-1967, "Power Piping" 8.15 Attachment A to Form 7, ECP-13-000947 Rev. 0 8.16 Shigley's Mechanical Engineering Design, Ninth Edition, Budynas & Nisbett 8.17 ASTM A53 "Standard Specification for Pipe, Steel, Black and Hot-Dipped, Zinc-Coated, Welded and Seamless" Page 24 of 24

TEAM INDUSTRIAL SERVICES, INC.

TECO MANUFACTURING, INC.

E~ng~iheer 4gGd~e0, der ltem#/SWO#

ECO#

NCR#

Letter Category 283380EM I

141781 01 IB jNuclear-Safety Related Requested Change

1. Remove Confidential & Proprietary note off of drawing and caics Reason for Change lCustomer Request D] QC Final Inspection Required Changed by JHH Change date 111/13/2013 Checked by IRD Checked date 111-13-13

• Approved by

[RD !

• Approval date 111/13/2613

• Approval Requiredfo IstfetyýiRelatedo AIOKý Effect On Structural Integrity of Clamp N/A Changes Made B1. Void Drawing B2. Add Drawing

83. Void Calcs B4. Add Calcs Manufacturing Received By QC Received By Date 1

Date I

I F1 Stock Item

I T E A M ] Industrial Services, Inc.

Registration # F-003143 Engineering Change Order Request Requested By: CUSTOMER Drawing # / Engineering Order #: 283380EM Department: BRANCH 204 Branch Job #: 204-10335 Received By: HH Date Effective: 11/13/13 Date: 11/13/13 Olmmediate I-Phase In -]Record only Description of Change:

1. Remove the Confidential and Proprietary note on the Drawing and Calcs 2.

3.

4.

5.

6.

Reason For Change:

1. CUSTOMER REQUEST 2.

3.

4.

5.

6.

03-24-11

HT-E Industrial Services Registration# F-003143 Engineering Department. Tel: (281) 388-5695 Fax: (281) 388-5690 ROUTING SLIP & COVER SHEET FOR NUCLEAR SAFETY RELATED JOBS Branch Work Order #: 204-10335 Customer: CCNPP Status: Priorit_

Caller: DAVE REDFIELD

_Safety Review_#:_283380 IEngr Order #: 283380EM _

Data Taken By:

Designed By:

Verified By:

Shop Received By:

QC Received By:

Name:

Adrian Williams Adrian Williams Mike Bautsch Simon Labrosse-Gelinas Heather Hodges _.......

Simon Labrosse-Gelinas Heather Hodges Adrian Williams Mike Lowe Roy Delgado Signature:

Date:

10/14/2013 10/14/2013 10/31/2013 11/1/2013 11/08/2013 10/14/2013 10/31/2013 11/1/13 11/4/13 11/8/13 Time:

3:15 pm 4:45 pm 3:30 pm 8:00 pm 10:45 am 7:30 pm 8:45 pm 3:15 PM 11:30 am Specifications:

Design Pressure:

50 psi Service:

SALT Total Weight:

233.7 1 Sealant Type:

1. 6 & G WATER b

)-FIBER

-Design Temperature:

Torque Value:

Void:

Maximum Injection Pressure:

95 OF 25 ft-lb; (+/--1.5 fi-lb) 26.3 in3 BC 1i05 PSI + STATIC QC FINAL INSPECTION REQUIRED Nuclear - Safety Related CMTRs and COCs Required PMI Required Bill of Materials:

==

Description:==

CLAMP CLAMP STUDS CLAMP NUTS Material:

SA 182 GR F316________

SA 193 GR 138M CLASS 1 Qty:

2 HALVES 16 32 232 INCHES 20 SA 194 GR 8M TUBING INJECTION VALVES STAINLESS STEEL STAINLESS STEEL DRILL THRU PLUGS STAINLESS STEEL 4

WASHERS SA 240 / 479 GR 316 16 PIPE PLUG STAINLESS STEEL I

ECO# 14170 A

11/11/2013 ECO# 14178 B 11/13/13 Rev. 3/3/2010

[fit t!.Z I It, Do "SAFETY FIRST - QUALITY ALWAYS" I

0 3/4" A

5/8" STUDS (16) PLACES TORQUE: 25 FT*LB (+1.5 FT*LB)

I-7-1/2" 1.

2.

3.

4.

5.

6.

7.

0 8.

9.

10.

11.

12.

13.

14.

15.

APPROVED TO MANUFACTURE 3/16" X 0.09" TUBING GROOVES IN BORES AND SIDEBARS 1/4" X 1/8" SEALANT GROOVES IN BORES & SIDEBARS INSTALL STAINLESS TUBING DRILL & TAP (8) 1/8-NPT INJ PORTS IN SIDEBARS DRILL & TAP 6 1/8-NPT INJ PORTS IN EACH ENDPLATE DRILL & TAP 4 1/4-NPT INJ PORTS IN CAVITY (DO NOT DRILL THRU)

(2) HALVES REQUIRED ALL DIMENSIONS ARE TYPICAL UNLESS NOTED COMMERCIAL GRADE DEDICATION REQUIRED BY TEAM NUCLEAR SAFETY RELATED DO NOT WELD; DO NOT PAINT PMI REQUIRED SEND WITH (1)1/2" PIPE PLUG SEND WITH (16)1/2" THICK WASHERS, 1-1/16" OD WITH 11/16" CENTERED THROUGH HOLE B ECO# 14178 (B2) ADD DATE: 11/13/13 A ECO# 14170 DATE: 11/11/13 T E A M Industrial Services, Inc.

REGISTRATION # F-003143 PERIMETER VOL 263 INA3 BRC ENGINEERING ORDER# 283380EM NT. 233.7 LB&kOL INA3 BC DRAWING # N/A TECO PART #

N/A WPS: NOT ALLOWED DRAWN BY: ABW/MB/SLG/HH1 11/8/2013 UNLESS O ERWMWE SPECIFIEC MACHINED SURFAME BREAKSýAP CORNEBS TOLEANMCES:

FRAC'ONAL 21/32 ANGULAR 1/2' JAO PALCE DECIMAL

,U.l DEREE PLACE DECIMAL A0D.M

&LL DIENSON $ N INCHES CCNPP LINE ENCLOSURE SIZE A

REV B

CHECKED BY:SLG/HH/ABW 11/1/2013 SCALE: 1:8 SHEET 1 OF 1

Dli*iliF Industrial Services, Inc.

Sheet 1 of 1 Registration # F-003143 MATERIAL SPECIFICATIONS El Non-Critical/Nuclear 0 Critical/Nuclear Drawn By: ABW/MB/SLG/HH Date: 11/4/13 Engineering Order No.:

283380EM Checked By: SLG/ABW/MGL Date: 11/4/13 Enclosures Material Specification CMTR COC NR PIPE FITTING ROLLED PLATE BLOCK / PLATE / SIDEBARS SA 182 GR F316 X

X ENDPLATES STRONGBACK BARS S.B. EARS/FINGERS_

Fasteners STUDS ENCLOSURE SA 193 GR B8M CLASS 1 X

X STUDS STRONGBACK NUTS ENCLOSURE SA 194 GR 8M X

X NUTS STRONGBACK SET SCREWS HTS I

FLANGE TEE RUN (if fabricated)

BRANCH (if fabricated)

FITTING WELD-O-LET VALVE FES Miscellaneous TUBING STAINLESS STEEL X

INJECTION VALVES STAINLESS STEEL X

X DRILL THRU PLUGS STAINLESS STEEL X

X WASHERS SA 240 / 479 GR 316 X

X PIPE PLUG STAINLESS STEEL X

X I

I I

I I

I 05/26/2009

From:TEAM IND SERVICES 8568324424 10/14/2013 14:51

1. 341 P.001/005 S171 i [0 Industrial Services,, Inc.

DAVE:

856-628-2817 LRS ENGINEERING DATA COVER SHEET Form 901.4 R2 fII '111 '*

Branch Work Order #:

Engr Order #:

283380E en Routine: U Priority:

Customer, pp,,

LRS: 0 PRP: 0 Other.

Safety Review #l(CJ):

Customer #:

Ship To:

Existing BP #:

T~hniclan Name(s)/

Date:

Operations I Tech Support Rep (If Applicable):

PRESSURE TEMPERATURE Design:

Design: Q 7

MDMT:

Service:

? (

(ndnAmumd aignnmeWutemp)

Operating:

3 S Operating:

1? 5 Line Material:

Flange Rating:

Schedule:

Line Size:

Quantity:

Se Selection:

Material Requested:

Package Requirements:

(Check all that are immediately needed) rCheck one only)

Y-Drawings L.

For Immediate Manufacture rr Calculations Wait for Approval of Package / Price q

Price (If so

]

ballpark or r-] by engineering)L Price Only / No Calculations/Drawings Date and Time Required:

E] Job is competitive bid Fax/Emai Prints and Calculations: (PLEASE PRINT CLEARLY)

D To Customer Name:

Fax No:

F To Branch E-mail: __Ay,, )

-4 *t

' i 1S#4 I

To Other O

Notify Branch Supervisor after faxing Name:

Phone No:

Li Immediately

[I Next Business Day Special Requirements:

[

Strongback needed for separation?

L Stress Relief Required by Customer

[

Strongback needed for vibration?

FI PE Stamp

[

Are there specific codes or additional requirements for this customer?.

[

CRN Province:

[] Weight concern? Customer target weight? __

ME TYPE:

Li Are weight supports needed? How much weight per support?

MTR'S OR COC'S Li If Lifting Lugs are required, where should they be located?

L Charpy -_

ft-lb at -

°F OtherDijRA1jM4

• 1LVf jPok-r

,f4 VvIle)-

1/2" d&t-NOT 3/4" PRPPRODUCTS Type of construction:

Seal Material:

Other Requirments:

[

Solid Block

[] Buna-N Li Anodes Life:

Qty __

L Welded Construction Li EPDM L Coating Li Casting L Afias L Hinges R

Banded' L Viton L Vent Valve Size__

L Other Li Other IL Other

From:TEAM IND SERVICES 8568324424 10/14/2013 14:52

1. 341 P.002/005 Froni:TEAM ND SERVICES 8568324424 10/14/2013 14:52

1. 341 P.002/005 DS 137 STRAIGHT LINE ENCLOSURE GIVEN BY:

t K' DATE:

/6 -l/9 -/*3 PLANT: I

-"N"P' I UNIT:

j;2 CHKD. BY:

_)

DATE:

I / o 3--/

3 SURFACE CONDITION:

4, OoL)

LINE SIZE:

)d SEVERITY OF LEAK:

I-ON 10, SHIP TO:

DIMENSIONAL DATA I

7.5" OEP-OEP MAX STAIGHT LINE LANDING BTWN THE FLG AND LUG.

OBSTRUCTIONS ENCLOSURE.

NO LTR.

Al BI Cl DI Wl W2 A2 B2 C2 D2 DIM.

.bi ?yk 6 OEP-OEP IS OKAY CBPTC)

B1 (MTAO) -

A!

B2-e(BPTC)

A2 i' (MTAO)

LOCATION OF BLOW:

-3 e5'e*of..<

OBSTRUCTIONS I

NOTES VIEW A-A do not drill specific d/t thru void (besides the.

hole)

COPYRIGHT 2000. Team Industrial Services. 5/06/03

From:TEAM IND SERVICES 8568324424 10/14/2013 14:53

1. 341 P.003/005 ARTICLE IX-3000 DESIGN REQUIREMENTS IX-3100 GENERAL DESIGN REQUIREMENTS The following design requirements shall be included in a Repair/Replacement plan and shall be considered in the analyses of the clamping device (lX-3200) and piping (IX-3300).

(a) Requirements to address environmental and corro-sive effects of seal composition, seal installation, and system fluid on piping, clamping device, and bolting.

(b) The defect size used in the design of the clamping device shall include any projected growth.

(c) If additional supports are required to satisfy IX-3200 or IX-3300, they shall be considered non-pressure-retaining items and shall be designed in accordance with the requirements of the Construction Code for the system or as permitted by IWA-4220.

IX-3200 CLAMPING DEVICE The following additional requirements apply to the design of the clamping device.

(a) No credit shall be taken for structural capability of the seal.

(b) Pressure retaining clamping device items shall be designed based on a stress analysis using the stress limits identified in Table IX-3200-I for the loading conditions specified in the Owner's requirements for the system.

(c) The clamping device shall be mechanically con-nected to the piping. Seal welds may be added to prevent leakage. Serrated contact surfaces of the clamping device are acceptable, provided they do not affect the structural integrity of the piping.

(d) If the clamping device is designed to carry, by friction, longitudinal loads normally transmitted by the piping, including postulated full circumferential sever-ance of the piping at the defect location, it shall be designed to produce clamping friction of at least five times the friction load required to prevent slippage. If a TABLE IX-3200-1 STRESS LIMITS FOR DESIGN AND SERVICE LOADINGS Service Limits Stress Limits11D Design and Level A (Normal) cr, < 1.0 S orn + ub < 1.5 5 Level B (Upset) orm< 1.10 S or, + o'b < 1.65 S Level C (Emergency) ar,, < 1.5 S din + orb < 1.8 S Level D (Faulted) a,, < 2.0 S v,,+

at, < 2.4 S NOTES:

(1) The symbols used in Table IX-3200-1 are defined as follows:

u' = general membrane stress, psi (kPa). Average stress across the solid cross section produced by mechanical loads; excludes effects of discontinuities and concentrations.

o'b = bending stress, psi (kPa). Linearly varying portion of stress produced by mechanical loads; excludes effects of discontinuities and concentrations.

S = allowable stress value, psi (kPa), at temperature, provided in the Construction Code.

coefficient of friction greater than 0.3 is used for friction-type connections, the coefficient of friction for each inter-face design (e.g., serrated or nonserrated), and each com-bination of interface material P-Numbers, shall be experimentally determined.

IX-3300 PIPING SYSTEM The following additional requirements apply to the evaluation of the piping system.

(a) Piping system vibration shall be considered when vibration is the apparent cause of the defect or the defect can be propagated by vibration.

(b) The piping system configuration with the clamping device shall be evaluated in accordance with the Owner's requirements. and either the Construction Code or Section III.

318

From:TEAM IND SERVICES

. 8568324424 10/14/2013 14:53

1. 341 P.0041005 IX-3300 MANDATORY APPENDIX IX IX-3300 (c) Effects of the stiffness and weight of the clamping device shall be considered in the evaluation of the piping systems. When the defect is caused by erosion or corro-sion, the base material thickness at the load trnusfer area shall be determined and projected to the time of removal of the clamping device. The projected wall thickness shall 319 be used when evaluating the piping system.

(d1) Constrainring effects of the clamping devicc shall be considered when evaluating effects of thermal expan-sion of the piping system.

(e) The Owner shall consider the effect of the defect and its expected growth, in the piping system evaluation.

From:TEAM IND SERVICES 8568324424 10/14/2013 14:54

1. 341 P.005/005 Quality System Supplement Corporate FORM 104.2 Rev: 6 Page I of 2 I

NUCLEAR AUTHORIZATION CHECKLIST (NACL) - TMS Division

• PART A: Use to document Contract Review for material only orders and in conjunction with PART B for service related work.

Submitted by:

)-.

Branch:

626C Date:

/0

/-N/-) -3 Team Job #:,02q./a 2 3 1 Customer ContractlWO#/PO#:

Utility:

/V e, Plant / Location: ai._

/

4

,c A evc.wl &/,4;ontact: & A 'r dci

)JA Phone #:

Personnel:

1.,f[q,*'4,,

2. 0.. 4 )q)<

3.

4.

Shift:

I Additional Personnel:

-4I~l MASO A' Afb&WA-t*'

oIIIWWIO' 1.

2.

3.

All Pre-Job Steps must be initialed by the Team Industrial Services, Inc. technician who is leading activities at the work site prior to performing any work.

The Owner Representative must initial Step 8prior to any work being performed.

All TEAM employees on the job must sign Step #12 Drior to any work beinz performed.

1. Has JSA been compleed9?

11 El f-

ý4rf

2. Has Tech. Support been contacted? (Critical Job Review) m" 03 13

'r 4

CJ#:

3 36*'.)

3. Have Team personnel READ and do they UNDERSTAND the Owner

['

I]

[

Engineering Control?

, q E.C. #:

4. Have Team personnel verified procedure(s) to be used9 9

El El 01-Procedure#;

V7,i~

5.

Have Team personnel READ and UNDERSTOOD the Owner W.O.

2 EI El A

.O Scope?

Er Ale-

/

6.

Have Team personnel been briefed on Owner W.O. Scope and received El El copy of WO.?

09= --

7. Have Team personnel had a Rad. Protection Brief?

'0 1] 'o -IV

8.

Has Owner Representative verified all Steps have been pefformed?

.erRep.

tolnitia..

9.

Materials:

3Q Certificate oflCAnforisance (COQ:

Yes [1 No El 10 Shiptz:

Seice:

SpecialHandlgsRequirements:

Ye s El No 2-

11. Additional Requirpnrts/CoPments:

3ff)

.n 4

'aie

12. Signatures of all TeaD PersoSnel:

P Seaan yL I I I It Service Line: _tsAIe T

oJAf Leak Severity:

Notifiations:

Safety Related:

Yes D No a

L ste S t

pec ieri ce r

Quality Assurance: Yes No [o i,

I l

Health Physics:

Yes g No NE]

Unit: TehExp.

Rate:

,Jntl b,

Procedures#:

Meia f

I

//ent3co Rev. M N

Op. Temnp:

OP. Press:

z_.Materials & Eguipment" Design Temp:

einPes Sealant Type:

Lot #

Equip. ID #:

/M,

Lot#:"£7 050%2

• /

Sealant Type:

• " F/544--

o Comnt'esrpio f o:Fabrication

• Data ComeW~scipio o Jb:Mill Tests: Yes ({fNo El I

c. IIIh Yes El No E Has the Customer expressed mechanical integrity concerns for the component?

E Yjs ]

No [A IPlant Rep. (print):

$r--,*

I,.o.,.

Initials: )ý5fg Design Calcs.'. Yes g Nor"]

Engr. Dw2s.: Yes ff No E]

TISI Tech. (print):Dow,o) *keori--

'I Initials:

CL)6,..

Positive Material Identification:

Yes sEf"No["]

Designer ABW/MBISLGIHH Date: 1118113 TEAM Industrial Services Sheet I of 6 Checker SLGIHHIABWiMGLIRD Date 283380EM 1118113 Split Circular Endplate Analysis B ECO# 14178 DATE: 11/13/13 (B4) ADD

References:

ASME Boiler and Pressure Vessel Code,Section II, Part D, (Table for Maximum Allowable Stresses, 2004 Edition Formulas for Stress and Strain by Roark and Young, Fifth Edition, Table 24, Case 31 Froo Data:

Design Pressure Design Temperature Split Endplate OD Cover Wall Thickness Split Endplate Thickness Opening Hole Diameter (Conservative)

Maximum Allowable Stress Inside Radius P:= 50.psi T := 95-deg OD:= 15.0.in twall := 0.5-in tendpl := 1.0. in HD:= 10.0.in Sa,1ow := 20000-psi IR:= [OD - 2(twa,,)]

2 Modulus of Elasticity Poisson's Ratio Maximum Allowable Deflection Joint Efficiency External Corrosion Allowance Intemal Corrosion Allowance OD := OD - 2.ExtCA twal, := twal - ExtCA - IntCA tendpl := tendpI - ExtCA - IntCA 8

E:= 0.276654.10.psi, v:= 0.31 Yma.,:= 0.05.in JE:= 1 ExtCA := 0.in lntCA := 0.in OD = 15.in twall 0.5.in tendpI = lin IR = 7.in Note: "OD" is based on the inside cavity +

2 x times the minimum wall thickness.

Analysis:

Solving for Modulus of Rigidity E

2-(1 + u) 7 G = 1.056 x 10.*psi Solving for variables OD - 2'twan a

2 b:= a - c REGISTRATION # F-003143 HD a -

2 C.-

2 a = 7-in b = 6.in c= 1-in

TEAM Industrial Services Sheet 2 of 6 283380EM Solving for Constants K:= 0.42338

-c)

, 1.58614.

+ 2.85046.

3.1727.*

+ 2.4848

+ c 1.0 c)

K = 1.205 1-bJ3

+ 4.(1 -

625.teIndpi G.(

+ b)2

'Y 1+

1-4b 2 24 XY2:=

_FnP~.

2

+

4 1X

- f 1 2 + X1 }(b 1-2).tah (1 2 7 B ECO# 14178 DATE: 11/13/13 (134) ADD

-y= 7.964 yli = 7.928 12 = 0.757 XI = 51.431 X= 0.115 c=

1.551 x 10 -

I CI :=

bI

)_(

l

)-cosh;-

C

(

2J I

C2 :=

C2 = 0.013 b -

Y2 2).(l -

I cosh 1 -

C X

(2J Stress at A (maximum) at':= 6-- c}Ci.(

-I

+ c'.,

-Y2 2. c tendpl Deflection at B (maximum) 24.P.c2*. b2.(t

.).(,c.cosh (.I I

-T,.+C.,osh1(2_71

+

E.tendpl 3 c

J b)

Minimum Cover Wall Thickness P-IR P.IR treqd :=

+

2JE-Sallow + 0.4-P JE-Sallow - 0.6.P at= 2196.938.psi S,,.,= 20000-psi y = 0.002.in Ymax = 0.05.in (Ymax is assumed based on testing) treqd = 0.02627-in twall = 0.5-in REGISTRATION # F-003143

TEAM Industrial Services Sheet 3 of 6j 283380EM Line Enclosure Analysis B ECO# 14178 DATE: 11/13/13 (B4) ADD

Purpose:

This analysis will calculate the internal stresses and bolt load of a line enclosure.

References:

ASME Boiler & Pressure Vessel Code,Section II, Part D, (Table for Maximum Allowable Stresses), 2004 Edition ASME Boiler & Pressure Vessel Code,Section III, ND-3324.3 Case B Team Industrial Services, Teco Manufacturing, Engineering Department, ISO-9001 Quality Manual, EP8.7

,ýR2 i

Dimensions Free Body Diggrom Data:

Design Pressure Design Temperature Inside Radius R := IR - IntCA Cover Thickness t := twall + IntCA Cavity to Stud CL End of Sidebar to Stud CL Sidebar Thickness P = 50.psi T = 95.deg R = 7-in t = 0.5-in A:= 0.75-in B := 0.78125-in ts := 2.8125-in ExtCA = 0.in IntCA = 0in Length Between Centedine of Seals Sidebar Length (at Centerline)

1. of Studs per Half Hole Size Stud Tensile Area Stud Allowable Stress Enclosure Allowable Stress LS:= 15.625.in LB:= 16-in NS2 := 8 h := 0.75.in TA:= 0.226-in2 s := 18800.psi Sa,(ow = 20000. psi Extemal Corrosion Allowance Internal Corrosion Allowance R := R + IntCA t := t - ExtCA - IntCA A:= A-IntCA R

T 7in t = 0.5-in A =0.75.in B := B - ExtCA LB := LB - 2.ExtCA ts:= ts - ExtCA B = 0.781.in LB = 16-in ts = 2.813.in REGISTRATION # F-003143

TEAM Industrial Services Sheet 4 of 61 283380EM I Analysis:

Solving for forces and moments F:= P.R.LS F,:= F 3

3 F = 5.469 x 10.-bf F, = 5.469 x 10.1bf Setting forces in x direction equal to 0 R2 := Fx, R2 = 5468.75.lbf B ECO# 14178 DATE: 11/13/13 (B4) ADD F,:= F 3

FY = 5.469 x 10.*Ibf Setting moments around centerpoint of cavity equal to 0 t

A+ B--

2 BL'= F-B Allowable Bolt Load BLa:= TA.Ss.NS2 BL = 8968.75-1bf BLa 33990.4 Ibf BL := if(BL < F,F,BL)

BL = 8968.75.lbf Stresses in Shell (thin walled enclosure)

P.R P.R a:= -

+ -

o-1050. psi t

2.t Sidebar Stress R,:= BL - F (at Bolt Centerline) 3 R,= 3.5 x 10.*lbf ts RI.B-.

2 O'b2 :

-1 2.-(LB - NS2.h).ts3 12 3

F Ts =-

2 (LB - NS2.h).ts aWb2 = 207.407-psi T, = 291.667.psi Results:

Less Than Bolt Load BL = 8968.75.lbf Stresses in Shell (thin walled enclosure) a= 1050.psi Sidebar Stresses (@ bolt centerline)

Crb2 = 207.41-psi Shear Stresses in Sidebar Ts = 291.67-psi Allowable BLa = 33990.4-1bf Sallow = 20000-psi Sallow = 20000.psi 0.8'Sa,1ow = 16000.psi REGISTRATION # F-003143

TEAM Industrial Services Sheet 5 of 6 283380EM Torque Analysis: 518" STUDS - Max Torque

Reference:

An Introduction To The Desiqn And Behavior Of The Bolted Joint by Bickford, Data:

Second Edition, Page 133.

Stud Tensile Area TA = 0.226. in2 Stud Allowable Stress Ss= 18800.psi Allowable Strength of Stud Fp := TA.Ss Fp = 4248.8-lbf Torque Application Factor A := 0.60 A ECO# 14170 Date: 11/11/11 (A3) ADD B ECO# 14178 DATE: 11/13/13 (B4) ADD Pitch of Threads Coefficient of Friction Nut/Stud Effective Contact Radius of Threads Half Angle of Threads Coefficient of Friction Nut/Joint Effective Contact Radius Nut/Joint Pitch := --- in 11 lit := 0.15 rt := 0.2822.in 3:= 30.deg Vin := 0.15 m := 0.4219.in Analysis:

( itch Itrt +

"n*

Torque := Fp-A-.( --. + cos(13) +

tn'M)

Torque = 26.9 ft-lbf OR Torque = 322.821.in.Ibf Torque Analysis: 5/8" STUDS

Reference:

An Introduction To The Desigqn And Behavior Of The Bolted Joint by Bickford, Data:

Second Edition, Page 133.

Stud Tensile Area TA = 0.226.in 2 Stud Allowable Stress Ss= 18800.psi Allowable Strength of Stud Fp := TASs Fp = 4248.8-lbf Torque Application Factor A := 0.55 Pitch of Threads Coefficient of Friction Nut/Stud Effective Contact Radius of Threads Half Angle of Threads Coefficient of Friction Nut/Joint Effective Contact Radius Nut/Joint Pitch := -

in 11 lit := 0.15 rt := 0.2822.in 0:= 30-deg Vin := 0.15 rn := 0.4219-in Analysis:

+

P itc tt.rt Torque := Fp.-2--

+-** cos(3- + an.m Torque = 24.66-ft-lbf OR Torque = 295.919.in.lbf REGISTRATION # F-003143

TEAM Industrial Services Sheet 6 of 6 1 283380EM Weight and Void Void Injection Valves NIV := 20 PERIMETER Void Calculations:

Void:

1.... in 2.(35.in - 0.75.in-16) + [(0.75.in)2 (0.5589-in 55625in) 16...

4 8

+ 1"1in2"(12.88-7r)-2.in + [(0.6875-in)2 (0. 55 8 9 -in) 2].4(0. 5.in). 3 2 4 8 4

Void = 22.746. in3 Void:= Void + (NIV.0.18.in 3)

Void = 26.346.in 3

Weight (Clamp Weight from SolidWorks Model)

Clamp := 98.851 Ib + 102.80. lb StudsNuts := 16-0.087-Lb 12.in + 32.0.11 -lb in B ECO# 14178 DATE: 11/13/13 (B4) ADD Clamp = 201.65.lb StudsNuts = 20.224.lb Washer = 1.12-1b Sealant = 1.458.lb InjValves = 10-1b DrillThruPlug = 0.44.lb Washer := 0.07.lb. 16 lb Sealant := Void. 1.35.0.041 l-b

. 3 in InjValves:= NIV.0.50-1b DrillThruPlug := 0.11lb.4 Weight := Clamp + StudsNuts + Sealant + InjValves + DrillThruPlug Weight = 233.772-1b REGISTRATION # F-003143

ATTACHMENT (2)

REGULATORY COMMITMENTS Calvert Cliffs Nuclear Power Plant, LLC November 14, 2013

ATTACHMENT (2)

REGULATORY COMMITMENTS The table below lists the action committed to in this submittal. Any other statements in this submittal are provided for information purposes and are not considered to be regulatory commitments.

Regulatory Commitment Date Verify that the installed mechanical clamping device is removed and replaced 04/01/2015 by a permanent code repair or component replacement.

I