Fig. 2.1.1.1. Locations of wear damage occurrence in Yonggwang Unit 3／4=10,47,1

Fig. 2.1.1.2. Locations of S／G tube failure & AVB set-up in Mihama Unit 2=10,47,1

Fig. 2.1.1.3. Photographs of wear-damaged S／G tubes=11,48,1

Fig. 2.1.2.1. The magnitude of the residual stress in the expanded region according to the expansion methods=19,56,1

Fig. 2.1.2.2. The magnitude of the residual stress at the inside and outside surface in the expanded region according to the expansion methods (mechanical roll,kiss roll,and hydraulic expansion)=19,56,1

Fig. 2.1.2.3. Residual stresses at inside and outside tube in the expanded region by a explosive expansion=20,57,1

Fig. 2.1.2.4. Change in residual stress in the expanded region by denting occurred in the TTS=20,57,1

Fig. 2.1.2.5. Change in residual stress in the expanded region by sludge deposition at TTS,(a) outside tube surface,(b) outside tube surface=21,58,1

Fig. 2.1.2.6. A diagram showing that the sludge deposition region is same as a location where the primary and secondary side SCC occurred in the Korean Standard Nuclear Power plant steam generator=21,58,1

Fig. 2.1.4.1. Photo of the degraded area adjacent to CRDM nozzle #3 in Davis-Besse nuclear station=28,65,1

Fig. 2.2.1.1. The assembly of the working electrode in the calculation of noise resistance=35,72,1

Fig. 2.2.2.1. General concept of structural integrity evaluation=39,76,1

Fig. 2.2.4.1. A schematic of a heat transfer crevice between the tube and tube sheet=48,85,1

Fig. 2.2.4.2. Percent of US PWRs using different strategies for water treatment from 1985 through 1998=49,86,1

Fig. 3.1.1.1. (a) Tube surface after mechanical hard rolling (Kori-1),(b) Mechanical (Hard rolling & Kiss rolling)- Ulchin-1,(c) Explosive rolling Ulchin-4=72,109,1

Fig. 3.1.1.2. Schematic of a re-circulating type U-tube steam generator=73,110,1

Fig. 3.1.1.3. Variation of tube vibration amplitude as a function of flow velocity in the steam generator=74,111,1

Fig. 3.1.1.4. Type of wear=74,111,1

Fig. 3.1.1.5. Vingsbo and Soderberg' fretting map=75,112,1

Fig. 3.1.1.6. Results of mass loss by NRC tests=75,112,1

Fig. 3.1.1.7. Comparison of mass losses of four combinations=76,113,1

Fig. 3.1.1.8. Photographs of worn areas showing various types of damage=77,114,3

Fig. 3.1.1.9. Intergranular Cr-carbide morphologies of (a) SAH (solution annealed at 1150℃ for 1 hr),(b) SAH701 (solution annealed at 1150℃ for 1 hr,thermally treated at 700℃ for 1 hr),(c) AS (as-received),and (d) solution annealed at 1150℃ fpr 1 hr,t=80,117,1

Fig. 3.1.1.10. Dependence of weight loss on intergranular Cr carbide morphology=81,118,1

Fig. 3.1.1.11. SEM images of worn surface depending on intergranular Cr carbide morphology=82,119,1

Fig. 3.1.1.12. Force histograms between S／G tube and support plate=83,120,1

Fig. 3.1.1.13. Correlation between wear and the distribution of force components in a force signal=84,121,1

Fig. 3.1.1.14. Equivalent depth of wear of Alloy 600 tubing vs. tube-support reaction force for Alloy 600／carbon steel combination=85,122,1

Fig. 3.1.1.15. Effect of the ration of two orthogonal force components on wear=85,122,1

Fig. 3.1.1.16. Wear rate variation with frequency,impact force:39 N,tube／TSP diametral clearance:0.78 mm,material:carbon steel,preload:5.56 N=86,123,1

Fig. 3.1.1.17. Comparison of mass losses for different combined impact-sliding motions=86,123,1

Fig. 3.1.1.18. Variation of wear depth depending on the TSP shape=87,124,1

Fig. 3.1.1.19. Effect of tube support-land length on the wear=87,124,1

Fig. 3.1.1.20. Effect of diametral clearance on the wear rate of Alloy 600 tubing=88,125,1

Fig. 3.1.1.21. Variations of friction coefficient depending on total cycle increase=88,125,1

Fig. 3.1.1.22. Work rate model considering the modified friction coefficient=89,126,1

Fig. 3.1.1.23. Wear rate as a function of test duration=90,127,1

Fig. 3.1.1.24. Comparison of wear rates in-air and in-water tests=91,128,1

Fig. 3.1.1.25. Effect of temperature on fretting-wear rates=91,128,1

Fig. 3.1.1.26. Interpretation of Ko's data in terms of wear coefficient=92,129,1

Fig. 3.1.1.27. Fretting wear results obtained at 25,215 and 265℃=92,129,1

Fig. 3.1.2.1. Schematic diagram showing locations of the strain gauge in Alloy 600=108,145,1

Fig. 3.1.2.2. Schematic diagram showing locations of the strain gauge in Alloy 690=109,146,1

Fig. 3.1.2.3. Measurement position of residual stress by XRD in the explosive expansion series=109,146,1

Fig. 3.1.2.4. Photograph showing a Siemens D5000 XRD with a four circle=110,147,1

Fig. 3.1.2.5. Photograph showing an attachment of a tube sample=110,147,1

Fig. 3.1.2.6. Total residual stress of Alloy 600 at outside tube,(a) total circumferential residual stress,(b) total axial residual stress=111,148,1

Fig. 3.1.2.7. Total residual stress of Alloy 690 at outside tube,(a) total circumferential residual stress,(b) total axial residual stress=112,149,1

Fig. 3.1.2.8. Uniformity of the expanded region according to expansion method=113,150,1

Fig. 3.1.2.9. Total residual stress of Alloy 600 at outside tube,(a) total circumferential residua stress,(b) total axial residual stress at inside tube=114,151,1

Fig. 3.1.2.10. Total residual stress of Alloy 690 at outside tube,(a) total circumferential residual stress at inside tube,(b) total circumferential residual stress at inside tube=115,152,1

Fig. 3.1.2.11. Total circumferential residual stress of Alloy 600 at outside tube by hydraulic expansion according to the location with respect to TTS=116,153,1

Fig. 3.1.2.12. Total axial residual stress of Alloy 600 at outside tube by hydraulic expansion according to the location with respect to TTS=116,153,1

Fig. 3.1.2.13. Total circumferential residual stress of Alloy 600 at inside tube by hydraulic expansion according to the location with respect to TTS=117,154,1

Fig. 3.1.2.14. Total axial residual stress of Alloy 600 at inside tube by hydraulic expansion according to the location with respect to TTS=117,154,1

Fig. 3.1.2.15. Total circumferential residual stress of Alloy 690 at outside tube by hydraulic expansion according to the location with respect to TTS=118,155,1

Fig. 3.1.2.16. Total axial residual stress of Alloy 690 at outside tube by hydraulic expansion according to the location with respect to TTS=118,155,1

Fig. 3.1.2.17. Total circumferential residual stress of Alloy 690 at inside tube by hydraulic expansion according to the location with respect to TTS=119,156,1

Fig. 3.1.2.18. Total axial residual stress of Alloy 690 at inside tube by hydraulic expansion according to the location with respect to TTS=119,156,1

Fig. 3.1.2.19. Photograph for the C-ring stress corrosion cracking specimens=120,157,1

Fig. 3.1.2.20. Characteristics of the increase in stress by loading-unloading method=120,157,1

Fig. 3.1.2.21. Photograph showing in Alloy 600 HTMA,sensitized (600℃-48 hours) 150% Yield stress,0.1 M Na₂S₄O6(이미지참조),room temperature,48 hours (Specimen ID:6AS17)=121,158,1

Fig. 3.1.2.22. Photograph showing in Alloy 600 HTMA,sensitized (600℃ -48 hours) C-ring at 150% yield stress,0.1 M Na₂S₄O6(이미지참조),room temperature,24hours,(Specimen ID:6AS8)=121,158,1

Fig. 3.1.2.23. Relationship between applied stress and time to cracking on sensitized Alloy 600 C ring specimens (100%~170% Yield stress,0.1 M Na₂S₄O6(이미지참조),room temperature)=122,159,1

Fig. 3.1.2.24. Relationship between applied stress and time to cracking on sensitized Alloy 600 C-ring specimens (90%,100,120% Yield stress,0.1 M Na₂S₄O6(이미지참조),room temperature)=122,159,1

Fig. 3.1.2.25. Photographs showing SCC cracks in Alloy 600 HTMA,sensitized,C ring,0.1 M,Na₂S₄O6(이미지참조),room temperature. (A) 90% Yield stress,(B) 100% Yield stress,(C) 120% Yield stress=123,160,1

Fig. 3.1.2.26. Relationship between applied stress vs. SCC cracking time in Alloy 600 HTMA,C-ring,0.1 M Na₂S₄O6(이미지참조) (0.2M after 720hrs),at room temperature=123,160,1

Fig. 3.1.3.1. Schematic diagram of the autoclave for crack initiation test and the crack propagation tester connected to a primary water simulation test loop=132,169,1

Fig. 3.1.3.2. Dimension of reverse u-bend specimen for crack initiation test=133,170,1

Fig. 3.1.3.3. Dimension of tube compact tension specimen for crack propagation test=133,170,1

Fig. 3.1.3.4. Summary on the results of PWSCC initiation test up to 18,000hours=134,171,1

Fig. 3.1.3.5. Morphology of crack surfaces of alloy 600 HTMA archive tube crack propagation test specimens after 2,000 hours at 40MPa√m=135,172,1

Fig. 3.1.3.6. Comparison of crack surfaces for as-received,thermally treated and serration heat treated UCN3 archive tube crack propagation test specimens after 2,000 hours at 40MPa√m=136,173,1

Fig. 3.1.3.7. Fractographs showing the effect of stress intensity factor on the crack growth rate of UCN3 and YG5／6 archive tubes=137,174,1

Fig. 3.1.3.8. Primary water stress corrosion crack propagation rate of domestic steam generator archive tubes=138,175,1

Fig. 3.1.4.1. Schematic drawing of the reactor vessel head in Davis-Besse nuclear station=170,207,1

Fig. 3.1.4.2. Crack／corrosion morphologies on the damaged CRDM nozzles in Davis-Besse nuclear station=171,208,1

Fig. 3.1.4.3. Feasible model on PWSCC cracking and boric acid corrosion in a CRDM nozzle=172,209,1

Fig. 3.1.4.4. (a) Boric acid deposits found on Oconee unit 1 CRDM Nozzle #21,and (b) PT result on some Oconee unit 3 CRDM Nozzle=173,210,1

Fig. 3.1.4.5. Optical micrograph of typical axial crack viewed parallel to the axis of pipe (X100)=174,211,1

Fig. 3.1.4.6. Schematic drawing of the cracking locations in Alloy 600／182 weldment in a PWR type environment=175,212,1

Fig. 3.1.4.7. Intergranular stress corrosion cracking of Alloy 182 with secondary cracks. TS orientation=176,213,1

Fig. 3.1.4.8. Effect of crack orientation on crack growth rates of Alloy 182=177,214,1

Fig. 3.1.4.9. Effect of temperature on crack growth rates of Alloy 182. (K＝22-26 MPa√m)=178,215,1

Fig. 3.1.4.10. Influence of temperature on the max. crack growth rates in Alloy 182=179,216,1

Fig. 3.1.4.11. Effect of weld heats and stress intensity on crack growth rates of Alloy 182=180,217,1

Fig. 3.1.4.12. Corrosion rates vs. 1／T in H₃BO₃ solutions=181,218,1

Fig. 3.1.4.13. Corrosion rates vs. 1／T in H₃BO₃+(LiOH or KOH) solutions=182,219,1

Fig. 3.1.4.14. (a) Dimensions of CT specimens for PWSCC crack growth test,and (b) terminology used for orientation of cracks in the welded and cold rolled specimens=183,220,1

Fig. 3.1.4.15. Schematic diagram of the autoclave for crack growth test connected to a primary water simulation test loop=184,221,1

Fig. 3.1.4.16. Terminology used for orientation of microstructural examination in the welded and cold rolled specimens=185,222,1

Fig. 3.1.4.17. Optical micrographs showing the microstructres of (a) XY plane and (b) YZ planes in the Alloy 600 base metal=186,223,1

Fig. 3.1.4.18. Dislocation morphologies in the Alloy 600 base metal=187,224,1

Fig. 3.1.4.19. Optical micrographs showing the microstructres of (a) XY,(b) XZ,and (c) YZ planes in the fusion zone of the Alloy 182 weld=188,225,1

Fig. 3.1.4.20. (a) Dendritic solidification structure,and optical micrographs showing the solodofocation morphologies of (b) XY,and (c) YZ planes in the fusion zone of the Alloy 182 weld=189,226,1

Fig. 3.1.4.21. Dislocation morphologies in the fusion zone of Alloy 182 weld=190,227,1

Fig. 3.1.4.22. (a) Optical micrographs showing the microstructure of the heat affected zone of Alloy 600／182 weld,(b) and (c) the high magnified views of parts in (a) denoted by squares=191,228,1

Fig. 3.1.4.23. (a) SEM image of cellular dendrites,and (b) compositional variations across the cellular dendritic interfaces in the fusion zone of Alloy 182 weld=192,229,1

Fig. 3.1.4.24. (a) Low magnified,and (b) high magnified SEM micrographs showing the second phases in the Alloy 600 base metal=193,230,1

Fig. 3.1.4.25. (a) TEM bright field image of niddle type precipitates,and (b) representative TEM／EDS spectra,taken from a carbon extraction replica of Alloy 182 weld=194,231,1

Fig. 3.1.4.26. Selected area diffraction patterns taken from the needle type precipitates in the Alloy 600 base metal,identified as Cr7(이미지참조)C₃=195,232,1

Fig. 3.1.4.27. (a) TEM image and SAPD of intergranular precipitates in the Alloy 600 base metal and (b) their representative TEM／EDS spectra=196,233,1

Fig. 3.1.4.28. (a) Optical micrograph of the heat affected zone of Alloy 600／182 weld,and (b)-(d) SEM micrographs of the parts in (a)=197,234,1

Fig. 3.1.4.29. (a) Low magnified,(b) high magnified TEM images of new precipitates in the grain boundary in the heat affected zone of Alloy 600／182 weld,and (c) their representative TEM／EDS spectra=198,235,1

Fig. 3.1.4.30. Micro-beam diffraction patterns taken from the new precipitates in the heat affected zone of Alloy 600／182 weld,identified as a fee structure with lattice constant of a＝1.06 nm=199,236,1

Fig. 3.1.4.31. (a) Low magnified,and (b) high magnified SEM micrographs showing the various second phases in the fusion zone of Alloy 182 weld=200,237,1

Fig. 3.1.4.32. (a) Centered dark field image,(b) their representative TEM／EDS spectra,and (c) selected area diffraction pattern,taken from the intergranular precipitates in the fusion zone of Alloy 182 weld=201,238,1

Fig. 3.1.4.33. (a) TEM bright field image and (b) their representative TEM／EDS spectra,taken from the coarse and faceted particles in the fusion zone of Alloy 182 weld=202,239,1

Fig. 3.1.4.34. Selected area diffraction patterns taken from the coarse and faceted particles in the fusion zone of Alloy 182 weld=203,240,1

Fig. 3.1.4.35. TEM bright field images from a (a) carbon extraction replica and (b) thin film showing the small and round particles in the fusion zone of Alloy 182 weld=204,241,1

Fig. 3.1.4.36. (a) TEM bright field image and (b) their representative TEM／EDS spectra,taken from the striped and round particles in the fusion zone of Alloy 182 weld=205,242,1

Fig. 3.1.4.37. (a) TEM bright field image and (b) their representative TEM／EDS spectra,taken from the dark and round particles in the fusion zone of Alloy 182 weld=206,243,1

Fig. 3.1.4.38. (a) TEM bright field image and (b) its related SADP,taken from a TiO type oxide in the fusion zone of Alloy 182 weld=207,244,1

Fig. 3.1.4.39. SADPs taken from a TiO Type oxide in the fusion zone of Alloy 182 weld=208,245,1

Fig. 3.1.4.40. SADPs with B-[100] showing the effect of Al addition in TiO type oxides in the fusion zone of Alloy 182 weld=209,246,1

Fig. 3.1.4.41. Schematic diagrams showing the relative positions of diffraction spots in (a) fee system and (b) simple cubic (sc) system. (c) shows the effect of Al addition on the crystal structure system of TiO type oxide=210,247,1

Fig. 3.1.4.42. TEM images showing the morphologies of (NbTi)C and oxides in the fusion zone of Alloy 182 weld=211,248,1

Fig. 3.1.4.43. Summary of second phase precipitation in the Alloy 600／182 weld=212,249,1

Fig. 3.1.4.44. (a) Optical micrograph showing the locations of micro-hardness test,and (b) variations of micro-hardness values across the specimen=213,250,1

Fig. 3.1.4.45. Optical micrographs showing a (a) fatigue pre-crack before PWSCC test,and (b) PWSCC crack after PWSCC test,of a CT specimen (Alloy 182 weld) with T-S orientation=214,251,1

Fig. 3.1.4.47. Optical micrographs showing a fracture morphology after PWSCC test,of a CT specimen (Alloy 182 weld) with T-S orientation=215,252,1

Fig. 3.1.4.48. Average PWSCC crack growth rates of Alloy 182 weld with T-S,L-T and T-L orientations=216,253,1

Fig. 3.1.4.49. Fracture morphologies of (a) fatigue pre-cracking region,(b) PWSCC cracking region,and (c) impact failure region in the CT specimen with T-S orientation after PWSCC test=217,254,1

Fig. 3.1.4.50. Optical micrograph showing fracture morphologies of the various regions in the CT specimen of Alloy 600／182 weld=218,255,1

Fig. 3.1.4.51. SEM micrographs showing fracture morphologies of the various regions in the CT specimen of Alloy 600／182 weld=219,256,1

Fig. 3.2.1.1. Schematic of C-ring specimen of Alloy 600=237,274,1

Fig. 3.2.1.2. Electrochemical cell for C-ring experiment=237,274,1

Fig. 3.2.1.3. Electric voltage and current noise of background noise=238,275,1

Fig. 3.2.1.4. Potential and current noise transients produced by stress corrosion cracking=238,275,1

Fig. 3.2.1.5. Specimen surface micrograph before stress corrosion cracking=239,276,1

Fig. 3.2.1.6. Potential and current noise transients produced by stress corrosion cracking=239,276,1

Fig. 3.2.1.7. Specimen surface micrograph before stress corrosion cracking=240,277,1

Fig. 3.2.1.8. Potential and current noise transients produced by stress corrosion cracking=240,277,1

Fig. 3.2.1.9. Specimen surface micrograph before stress corrosion cracking=241,278,1

Fig. 3.2.1.10. Potential and current noise transients produced by stress corrosion cracking=241,278,1

Fig. 3.2.1.11. Specimen surface micrograph before stress corrosion cracking=242,279,1

Fig. 3.2.1.12. Potential and current noise transients produced by stress corrosion cracking=242,279,1

Fig. 3.2.1.13. Specimen surface micrograph before stress corrosion cracking=243,280,1

Fig. 3.2.1.14. Crack propagation speed of stress corrosion cracking=243,280,1

Fig. 3.2.1.15. Photograph of specimen cross section after stress corrosion cracking test=244,281,1

Fig. 3.2.1.16. Photograph of specimen fracture after stress corrosion cracking test=244,281,1

Fig. 3.2.1.17. Electrochemical potential and current noise peak of no stress corrosion cracking=245,282,1

Fig. 3.2.1.18. Noise resistance values of no stress corrosion cracking=245,282,1

Fig. 3.2.1.19. Localization index of no stress corrosion cracking=246,283,1

Fig. 3.2.1.20. Electrochemical potential and current noise peak of by stress corrosion cracking=246,283,1

Fig. 3.2 1.21. Noise resistance values of by stress corrosion cracking=247,284,1

Fig. 3.2.1.22. Localization index of by stress corrosion cracking=247,284,1

Fig. 3.2.2.1. COD changes of a part through wall axial defect=254,291,1

Fig. 3.2.2.2. Crack opening behavior of a 100% TW axial defect=254,291,1

Fig. 3.2.2.3. Crack opening behavior of 100% TW circumferential defect=255,292,1

Fig. 3.2.2.4. Crack opening behavior of 100% TW circumferential defect=255,292,1

Fig. 3.2.2.5. Crack opening behavior of 100% TW circumferential + axial defect=256,293,1

Fig. 3.2.2.6. Burst pressure of steam generator tubes with axial through-wall crack=256,293,1

Fig. 3.2.2.7. Burst pressure of steam generator tubes with axial surface crack=257,294,1

Fig. 3.2.2.8. Burst pressure of steam generator tubes with circumferential through-wall crack=257,294,1

Fig. 3.2.2.9. Comparison between predicted results and experimental results for tube with axial through-wall crack=258,295,1

Fig. 3.2.2.10. Comparison of limit load analysis results with fracture mechanics analysis results for axial through-wall cracked tubes=259,296,1

Fig. 3.2.2.11. Prediction results for axial through-wall cracked tubes based on limit load and fracture mechanics analyses=260,297,1

Fig. 3.2.2.12. Comparison between predicted results and experimental results for axial surface crack tubes=261,298,1

Fig. 3.2.2.13. Comparison of analysis results with test data results for axial surface cracked tubes=262,299,1

Fig. 3.2.2.14. Prediction results for axial surface cracked tubes based on modified fracture mechanics analysis=262,299,1

Fig. 3.2.2.15. Comparison between predicted results and experimental results for circumferential through-wall crack tubes=263,300,1

Fig. 3.2.2.16. Comparison of limit load analysis results with fracture mechanics analysis results for circumferential through-wall cracked tube=264,301,1

Fig. 3.2.2.17. Prediction results for circumferential through-wall cracked tubes based on limit load and fracture mechanics analyses=265,302,1

Fig. 3.2.3.1. Stress measurement apparatus(flexible strip bend method)=296,333,1

Fig. 3.2.3.2. Design of anode for electrodeposition inside steam generator tube=297,334,2

Fig. 3.2.3.3. Potentiodynamic curve obtained during electrodeposition in 1.39mol／1 Ni (SO₃ㆍNH₂)₂+0.65mo1／1 H₃BO₃+0.007mo1／1 H₃PO₃+0.005mol／l Fe(SO₃ㆍNH₂)₂solution of 50℃ at a scan rate of 10mV／sec as a function of pH=299,336,1

Fig. 3.2.3.4. Deposition rate and stress obtained for Ni-P-Fe electrodeposits as a function of pH in 1.39mo1／l Ni(SO₃ㆍNH₂)₂+0.65mo1／1 H₃BO₃+0.007mol／1 H₃PO₃+0.005mo1／l Fe(SO₃ㆍNH₂)₂ solution of 60℃=300,337,1

Fig. 3.2.3.5. Content of alloying element in the deposit and current efficiency obtained for Ni-P-Fe electrodeposits as a function of pH in 1.39mo1／l Ni(SO₃ㆍNH₂)₂+0.65mo1／1 H₃BO₃+0.007mol／1 H₃PO₃+0.005mo1／l Fe(SO₃ㆍNH₂)₂ solution of 60℃=300,337,1

Fig. 3.2.3.6. X-ray diffraction patterns obtained for Ni-P-Fe electrodeposits as a function of pH in 1.39mo1／l Ni(SO₃ㆍNH₂)₂+0.65mo1／1 H₃BO₃+0.007mol／1 H₃PO₃+0.005mo1／l Fe(SO₃ㆍNH₂)₂ solution of 60℃=301,338,1

Fig. 3.2.3.7. Potentiodynamic curve obtained during electrodeposition in 1.39mo1／l Ni(SO₃ㆍNH₂)₂+0.65mo1／1 H₃BO₃+0.007mol／1 H₃PO₃+0.005mo1／l Fe(SO₃ㆍNH₂)₂ solution at a scan rate of 10mV／sec as a function of temperature=302,339,1

Fig. 3.2.3.8. Deposition rate and stress obtained for Ni-P-Fe electrodeposits as a function of temperature in 1.39mo1／l Ni(SO₃ㆍNH₂)₂+0.65mo1／1 H₃BO₃+0.007mol／1 H₃PO₃+0.005mo1／l Fe(SO₃ㆍNH₂)₂ solution=303,340,1

Fig. 3.2.3.9. Composition of alloying element and current efficiency obtained for Ni-P-Fe electrodeposits as a function of temperature in 1.39mo1／l Ni(SO₃ㆍNH₂)₂+0.65mo1／1 H₃BO₃+0.007mol／1 H₃PO₃+0.005mo1／l Fe(SO₃ㆍNH₂)₂ solution=303,340,1

Fig. 3.2.3.10. X-ray diffraction patterns obtained for Ni-P-Fe electrodeposits as a function of temperature in 1.39mo1／l Ni(SO₃ㆍNH₂)₂+0.65mo1／1 H₃BO₃+0.007mol／1 H₃PO₃+0.005mo1／l Fe(SO₃ㆍNH₂)₂ solution=304,341,1

Fig. 3.2.3.11. X-ray diffraction pattern for the Ni-P-Fe electrodeposit obtained under the conditions of a peak current density of 200㎃／㎠ and a duty cycle of 50% with a scan rate 4℃／min=305,342,1

Fig. 3.2.3.12. Stress-strain curves for the electrodeposits obtained as a function of the peak current density at the same duty cycle of (a) 30,(b) 50 and (c) 100%(DC)=305,342,2

Fig. 3.2.3.13. TEM micrographs for the electrodeposits obtained as a function of the peak current density at the same duty cycle of (a) 30 and (b) 50%=307,344,1

Fig. 3.2.3 14. Stress-strain curves for the electrodeposits obtained as a function of the duty cycle at a peak current density of 200㎃／㎠=308,345,1

Fig. 3.2.3.15. TEM micrographs for the electrodeposits obtained at a peak current density of 200㎃／㎠ as a function of duty cycle of (a) 30,(b) 50 and (c) 70%=309,346,1

Fig. 3.2.3.16. Stress-strain curves for the pulse-plated electrodeposit without an additive and the DC-plated electrodeposit with an additive=309,346,1

Fig. 3.2.3.17. TEM micrographs obtained from the electrodeposits (a) without and (b) with additive=310,347,1

Fig. 3.2.3.18. SEM micrographs obtained from strike layers as a function of the temperature forming the strike layer,(a) 40,(b) 50 and (c) 60℃=310,347,1

Fig. 3.2.3.19. Photograph obtained from 200㎛ thick Ni electrodeposit／5㎛ thick strike layer formed at 60℃=311,348,1

Fig. 3.2.3.20. Photographs obtained from various thick strike layers formed at 40℃=311,348,1

Fig. 3.2.3.21. SEM micrographs obtained from various thick strike layers formed at 40℃=312,349,1

Fig. 3.2.3.22. SEM micrographs obtained from the strike layers formed in strike forming solution with HCl and without HCl at 40℃=312,349,1

Fig. 3.2.3.23. SEM micrographs obtained from Ni electrodeposit + the strike layer formed in strike forming solution (a) with HCl and (b) without HCl at 40℃=313,350,1

Fig. 3.2.3.24. Schematic drawing of tensile test specimen for adhesion strength measurement=313,350,1

Fig. 3.2.3.25. Stress-strain curves obtained from tensile test specimens for adhesion strength measurement=314,351,1

Fig. 3.2.3.26. Potentiodynamic curves obtained from various Ni-P-B electrodeposit forming solutions with a scan rate of 10mV／sec=314,351,1

Fig. 3.2.3.27. Nyquist plots obtained during applying various current densities in Ni-P-B electrodeposition bath=315,352,2

Fig. 3.2.3.28. Equivalent circuit for electrodeposition system,where Re(이미지참조),C,Rt(이미지참조),p and L are the solution resistance,the double layer capacitance,the charge transfer resistance,the Faradaic resistance and self inductance,respectively=316,353,1

Fig. 3.2.3.29. Stress values measured for the electrodeposits prepared from electrodeposition solutions having various phosphorus acid concentrations using strip bend method at RT=317,354,1

Fig. 3.2.3.30. Stress values measured for the electrodeposits prepared from electrodeposition solutions having various saccharin concentrations using strip bend method at RT=318,355,1

Fig. 3.2.3.31. X-ray diffraction patterns obtained from the Ni alloy electrodeposits containing various P and B contents with a scan rate of 4℃／min=319,356,1

Fig. 3.2.3.32. TEM micrographs for the same specimens of Fig. 3.2.3.31=320,357,1

Fig. 3.2.3.33. TEM micrographs obtained from the Ni alloy electrodeposits without additives=321,358,1

Fig. 3.2.3.34. Vickers hardness of Ni-P-B electrodeposit as a function of heat treatment temperature=321,358,1

Fig. 3.2.3.35. TEM micrographs for heat-treated Ni-P-B electrodeposits=322,359,1

Fig. 3.2.3.36. X-ray diffraction patterns obtained from the Ni alloy electrodeposits with and without additives with a scan rate of 4℃／min=323,360,1

Fig. 3.2.3.37. TEM micrographs obtained from the Ni + 0.001M P alloy electrodeposits with and without additives,respectively=323,360,1

Fig. 3.2.3.38. Stress-strain curves obtained from Ni-P-B electrodeposits(0.007M and 0.001M as P and B sources) and chemical compositions as a function of additive content=324,361,1

Fig. 3.2.3.39. Stress-strain curves for Ni-P-B electrodeposits(0.07M and 0.001M as P and B sources) obtained during application of 100 and 200㎃／㎠ DC in electrodeposition bath of 60℃,pH 2 without additive=325,362,1

Fig. 3.2.3.40. Stress-strain curves for Ni-P-B electrodeposits(0.007M and 0.001M as P and B sources) obtained as a function of current density in electrodeposition bath of 60℃ pH 2 with saccharin of 35mg／l=325,362,1

Fig. 3.2.3.41. Stress-strain curves obtained from Ni-P-B electrodeposits(0.007M and 0.001M as P and B sources) and chemical compositions as a function of duty cycle in 60℃,pH 2 solution without additive=326,363,1

Fig. 3.2.3.42. TEM micrographs for Ni-P-B electrodeposits(0.007M and 0.001M as P and B sources) formed under application of duty cycle 30%(left) and 80%(right) in 60℃,pH 2 solution without additive=327,364,1

Fig. 3.2.3.43. Microhardness values obtained from Ni-P-B electrodeposits(0.007M and 0.001M as P and B sources) as a function of duty cycle in 60℃,pH 2 solution without additive=327,364,1

Fig. 3.2.3.44. Apparatus for electrodeposition inside tube=328,365,1

Fig. 3.2.3.45. Experimental flow chart=329,366,1

Fig. 3.2.3.46. TEM micrographs for Ni-P-Fe and Ni-P-B electrodeposits formed by Fig. 3.2.3.45 process condition=329,366,1

Fig. 3.2.3.47. Schematics of C-ring specimen=330,367,1

Fig. 3.2.3.48. Optical micrograph for 1% strained C-ring(normal and reverse directions) Alloy 600 exposed 315℃ ,10wt.% NaOH,564 hrs=330,367,2

Fig. 3.2.3.49. Optical micrographs for Ni-P-Fe C-ring specimens after exposure at 315℃ in 10wt% NaOH=331,368,1

Fig. 3.2.3.50. Optical micrographs for Ni-P-B C-ring specimens after exposure at 315℃ in 30wt% NaOH=332,369,1

Fig. 3.2.3.51. Optical micrographs for Ni-P-Fe and Ni-P-B reverse C-ring specimens after exposure at 315℃ in 30wt% NaOH during 1800hrs=332,369,1

Fig. 3.2.4.1. Shape and dimensions of the test sample employed=351,388,1

Fig. 3.2.4.2. Some examples of the stress-strain curve obtained from the SSRT tests=351,388,1

Fig. 3.2.4.3. SEM micrograph of fracture surface of a sample strained in 40% NaOH solution at 315℃. On the sample IG cracks were observed along the edge=352,389,1

Fig. 3.2.4.4. SEM micrograph of fracture surface of a sample strained in reference solution + (a) CeO₂,(b) (CH₃COOH)₃Ce,and (c) H₃BO₃ at 315℃=353,390,1

Fig. 3.2.4.5. SEM micrograph of fracture surface of a sample strained in reference solution + (a) CeB6(이미지참조),(b) NiB,and (c) FeB at 315℃=354,391,1

Fig. 3.2.4.6. SEM micrographs of gage surface of samples strained in (a) 40% NaOH solution (reference solution),(b) Group B (Ce),(c) Group C (B),and (d) Group D (borides) at 315℃. White arrows indicate IG cracks=355,392,1

Fig. 3.2.4.7. AES depth profiles of samples exposed for 5 days to (a) 40% NaOH solution (reference solution),(b) CeB6(이미지참조),and (c) NiB containing solutions at 315℃=356,393,1

Fig. 3.2.4.8. Depth composition profiles for Alloy 600 surface films exposed at 285℃ in pH 10 water for 168 hrs (a) 3.0g O₂／kg H₂O,(b) 0.15 mg O₂／kg H₂O,and (c) 0.005mg O₂／kg H₂O. [McIntyre et at,J. of Electrochemical Society,Vol. 126,No. 5 (197=357,394,1

Fig. 3.2.4.9. Narrow scan XPS depth spectra of samples exposed for 5 days to 40% NaOH solution (reference solution),CeB6(이미지참조),and NiB containing solutions at 315℃ (a) before cleaning and (b) after cleaning=358,395,1

Fig. 3.2.4.10. Current densities used to determine the corrosion current density in the four point method=359,396,1

Fig. 3.2.4.11. Polarization curves of Alloy 600 in 40% NaOH solution at 20℃=360,397,1

Fig. 3.2.4.12. Polarization curves of Alloy 600 in 40% NaOH solution at 315℃=360,397,1

Fig. 3.2.4.13. Polarization curves of Alloy 600 in 40% NaOH + CeB6(이미지참조) solution at 315℃=361,398,1

Fig. 3.2.4.14. Polarization curves of Alloy 600 in 40% NaOH + NiB solution at 315℃=361,398,1

Fig. 3.2.4.15. Polarization curves of Alloy 600 in 40% NaOH + CeO₂ solution at 315℃=362,399,1

Fig. 3.2.4.16. The values of corrosion current density in the various solutions along with SEM micrographs of the gage surfaces in the same solutions showing the presence or absence of IG cracks=363,400,1

Fig. 3.2.4.17. Some examples of the determination of the polarization resistance of Alloy 600 in 40% NaOH solution=364,401,1

Fig. 3.2.4.18. The values of polarization resistance of Alloy 600 in various solutions=365,402,1

Fig. 3.2.4.19. Stress-strain curves obtained from the SSRT tests in ammonia solutions with and without borides=366,403,1

Fig. 3.2.4.20. SEM micrographs of the gage lengths of the samples tested in (a) the reference solution (NH₃,pH＝9.5) (b) Ref. + 2g／l CeB6(이미지참조) (pH＝9.7),and (c) Ref,+ 2g／l NiB (pH＝9.7)=367,404,1

Fig. 3.2.4.21. AES depth profile of the surface oxides on the samples tested in the 315℃ ammonia solutions=368,405,1

Fig. 3.2.4.22. Estimated surface oxide thickness of the samples tested in (a) the reference solution (NH₃,pH＝9.5) (b) Ref. + 2g／l CeB6(이미지참조) (pH＝9.7),and (c) Ref,+ 2g／l NiB (pH＝9.7)=369,406,1

Fig. 3.3.1.1. Dimensions of rectangular strip and stressed U-bended specimens (a) rectangular and (b) stressed U-bend. (unit:mm)=383,420,1

Fig. 3.3.1.2. Temperature dependence of grain size of the model alloys after solution annealing treatment=384,421,1

Fig. 3.3.1.3. Optical micrographs of model alloys after solution annealing (a) 600CE0 at 975℃ for 20min,(b) 600CE4 at 1010℃ for 10min=385,422,1

Fig. 3.3.1.4. SEM micrographs showing grain boundary carbides in 600CE0 after thermal treated at 704℃ for (a) 1hr,(b) 15hr,(c) 48hr,(d) 96hr and 600CE4 after thermal treated at 704℃ for (e) 1hr,(f) 15hr,(g) 48hr,(h) 96hr=386,423,1

Fig. 3.3.1.5. Variations of the size and distribution of intergranular carbides precipitated in the model alloys with thermal treated time=387,424,1

Fig. 3.3.1.6. TEM micrographs and selected area diffraction pattern of the carbide precipitates of model alloy 600 after thermal treated at 704℃ for 15hr:(a),(b) 600CE0 and (c),(d) 600CE4=388,425,1

Fig. 3.3.1.7. TEM electro beam trace across a grain boundary and between carbides of (a) 600CE0 and (b) 600CE4 after thermal treated at 704℃ for 15hr=389,426,1

Fig. 3.3.1.8. Cr concentration profiles around grain boundaries of the model alloys after thermal treated at 704℃ for 15hr=390,427,1

Fig. 3.3.1.9. Stress-Strain curves of model alloy specimens determined at room temperature=390,427,1

Fig. 3.3.1.10. OM and SEM micrographs of cracks occurring in U-bend specimens tested in 40% NaOH solution at 315℃:(a),(c),(e) 600CE0 and (b),(d),(f) 600CE4=391,428,1

Fig. 3.3.1.11. Relationship between the maximum crack depth and exposure time=392,429,1

Fig. 3.3.1.12. Grain boundary carbides promoting crack blunting because of their effectiveness as a dislocation source [Br88]=393,430,1

Fig. 3.3.1.13. Comparison of the dislocation motion in (a) 600CE0 deformed 0.75% and (b) 600CE4 after deformed 0.75%=394,431,1

Fig. 3.3.2.1. SEM micrographs showing intergranular carbides (a) in the transverse cross section and (b) in the longitudinal cross section of as-pilgered Alloy 690=409,446,1

Fig. 3.3.2.2. Intergranular carbide morphologies in Alloy 690 heat treated at 1200℃ for 1 hr followed by subsequent heat treatment (a) at 1105℃ and (b) at 1108℃ for 1 hr,etched in 15 % H₃PO₄+85% distilled water=410,447,1

Fig. 3.3.2.3. (a) Optical micrograph of Alloy 690 heat treated at 1130℃ for 20 min.,etched in a nital solution and (b) grain size variation as a function of heat treatment temperature and time=411,448,1

Fig. 3.3.2.4. (a) Grain boundary Cr-rich M23(이미지참조)C6(이미지참조) carbides,and (b) the related SADP which shows the cube-cube orientation relationship with one grain=412,449,1

Fig. 3.3.2.5. Schematic diagram showing the heat treatment condition for serrated grain boundary formation in Alloy 690=413,450,1

Fig. 3.3.2.6. Effect of final heat treatment temperature on the degree of serration in Alloy 690. (a) 990℃,(b) 970℃,(c) 900℃,and (d) 800℃=414,451,1

Fig. 3.3.2.7. Schematic diagram showing the temperature range for serrated grain boundary formation in Alloy 690 with a carbon content of 0.03 wt%,an average grain size of 50㎛,and a cooling rate of 0.5℃／min=415,452,1

Fig. 3.3.2.8. Effect of cooling rate on the degree of serration in Alloy 690. (a) 100℃／min.,(b) 20℃／min.,(c) 2℃／min.,and 1℃／min=416,453,1

Fig. 3.3.2.9. Effect of average grain size on the degree of serration with a cooling rate of 2℃／min. (a) 70㎛ and (b) 35㎛=417,454,1

Fig. 3.3.2.10. Various grain boundary morphologies of (a) wavy,(b) serrated,(c) irregular type,and (d) grain boundary pinning found in the serrated Alloy 690=418,455,1

Fig. 3.3.2.11. Intergranular Cr carbide precipitation (a) in the serrated Alloy 690 with a cooling rate of 0.5℃／min.,and (b) In the thermally treated Alloy 690 at 720℃／min for 48 hrs=419,456,1

Fig. 3.3.2.12. Effect of cooling rate on the intergranular Cr carbide precipitation in the serrated Alloy 690. (a) 20℃／min.,(b) 5℃／min.,and (c) 1℃／min=420,457,1

Fig. 3.3.2.13. TEM bright field images showing interface dislocations due to a lattice mismatch on the coherent interfaces of two same crystal structures=421,458,1

Fig. 3.3.2.14. Formation of interface dislocation to accommodate a lattice mismatch on the coherent interface of two same crystal structure=422,459,1

Fig. 3.3.2.15. (a) SEM micrograph showing the different curvatures of intergranular carbides and grain boundary,and (b) schematic drawing showing the coherency of intergranular carbides with a grain boundary=423,460,1

Fig. 3.3.2.16. (a) TEM image around a straight grain boundary and (b) compositional variations across the grain boundary in Alloy 600=424,461,1

Fig. 3.3.2.17. Schematic diagram showing the growth directions of intergranular Cr carbides and the resultant degrees of chromium depletion around the grain boundary=425,462,1

Fig. 3.3.2.18. (a) TEM image around a serrated grain boundary and (b) compositional variations across the grain boundary in Alloy 690=426,463,1

Fig. 3.3.2.19. Schematic drawings showing the grain boundary migration from a coherent grain to a non-coherent grain in the serration treated Alloy 690=427,464,1

Fig. 3.3.2.20. Schematic diagram of a proposed mechanism on serrated grain boundary formation in Alloy 690=428,465,1

Fig. 3.4.1.1. Typical X-ray diffraction pattern for Ni electrodeposit obtained from 1.39mo1／l Ni sulfamate + 0.65mo1／1 boric acid solution at 60℃=435,472,1

Fig. 3.4.1.2. Plot of current efficiency against average applying direct current density=435,472,1

Fig. 3.4.1.3. Potentiodynamic curve obtained for Ni electrodeposit in 1.39mo1／1 Ni(SO₃ㆍNH₂)₂+0.65mo1／1 H₃BO₃ of 60℃ at a scan rate of 10mV／sec=436,473,1

Fig. 3.4.1.4. Vickers hardness obtained as a function of average current density=436,473,1

Fig. 3.4.1.5. Plot of current efficiency against duty cycle for Ni electrodeposits obtained by application of a peak current density=437,474,1

Fig. 3.4.1.6. Plot of victors hardness against duty cycle for Ni electrodeposits obtained by application of a peak current density,111mA／㎠=437,474,1

Fig. 3.4.1.7. Micrographs for Ni electrodeposit C-ring specimens after 14 days exposure without potential application,followed by 3 days exposure with potential application of 180mV above open circuit potential in 40% NaOH at 315℃=438,475,1