Fig. 17 Conventional SADP (a) and ZOLZ-CBEDP (b) in 316 stainless steel. The diffraction patterns were taken along the [111] zone axis. The two diffraction patterns are essentially identical and can be indexed using the same procedure. If the beam convergence angle in the CBEDP is increased More

Fig. 19 Kossel CBEDP from 316 stainless steel in which the diffraction disks overlap. Only the zero-order Laue reflections are visible in this image. Courtesy of M. Kersker More

Fig. 20 HOLZ pattern taken from 316 stainless steel. Only the FOLZ ring is present in the CBEDP. The HOLZ lines are also visible. Analysis of these patterns allows for precise determination of the three-dimensional crystallography of the specimen. Courtesy of M. Kersker More

Fig. 51 Stress-corrosion fractures in a 25% cold-worked type 316 austenitic stainless steel tested in a boiling (154 °C, or 309 °F) aqueous 44.7% magnesium chloride solution. At low (14 MPa m , or 12.5 ksi in .) K l values, the fracture exhibits a combination of cleavage More

Fig. 89 Typical fatigue fracture appearance in a cold-worked type 316 stainless steel tested at 593 °C (1100 °F) in air and vacuum. (a) The fracture in air was primarily transgranular with distinct fatigue striations. (b) The fracture in vacuum was predominantly intergranular with no distinct More

Fig. 91 Typical fatigue fracture appearance of an annealed type 316 stainless steel tested in vacuum at 25 °C (75 °F) (a) and 593 °C (1100 °F) (b). The crack propagation direction is from left to right. Small arrows point to the interface between the precracked region and the propagating More

Fig. 94 Fracture appearance of a cold-worked type 316 stainless steel fatigue tested in vacuum of 593 °C (1100 °F) under a 1-min dwell time. Note the more intergranular nature of this fracture when compared to Fig. 89(b) , which shows the fracture appearance of the same alloy tested under More

Fig. 74 Macrographs (top) and microstructures (bottom) of short-time type 316 stainless steel tensile specimens tested at various temperatures. Top, from left: specimens tested at 760 °C (1400 °F), 815 °C (1500 °F), 870 °C (1600 °F), 925 °C (1700 °F), and 980 °C (1800 °F). Bottom, from left More

Fig. 76 Microstructure and fracture appearance of type 316 stainless steel tested in creep to fracture in air at 800 °C (1470 °F) at a load of 103 MPa (15 ksi). Time to rupture: 808 h. Light micrographs (a and b) illustrate r-type cavities caused by vacancy condensation on boundaries More

Fig. 78 Microstructure and fracture appearance of type 316 stainless steel tested in creep to fracture in air at 685 °C (1265 °F) at a load of 123 MPa (17.9-ksi). Time to rupture: 710 h. The light micrograph (a) shows triple boundary cracking with extensive bulk deformation and grain More

Fig. 79 Microstructure and fracture appearance of type 316 stainless steel tested in creep to fracture at 770 °C (1420 °F) using a 62-MPa (8.95-ksi) load. Time to rupture: 808 h. (a) Optical micrograph showing crack nucleation and growth by decohesion along the carbide/matrix interfaces More

Fig. 650 Failure due to chloride stress-corrosion cracking (SCC) of an AISI type 316 pipe. The pipe served as a vent for the preheater-reactor slurry transfer line in a coal-liquefaction pilot plant. Although no material flowed through the vent line—a “dead leg”—the service temperature was low More

Fig. 21 Erosion rate of laser-modified 316 stainless steel (UNS 31603) 31603 stainless steel (frequency = 20 kHz; specimen mounted in vibration horn; vibration amplitude = 30 μm; temperature =23 °C; liquid: 3.5% NaCl aqueous solution). LA, laser alloyed; LM, laser modified. Source: Ref 42 More

Fig. 36 Section through type 316 stainless steel tubing that failed by SCC because of exposure to chloride-contaminated steam condensate. Micrograph shows a small transgranular crack that originated at a corrosion pit on the inside surface of the tubing and only partly penetrated the tubing More

Fig. 13 Weld in AISI type 316 heat-exchanger shell that failed due to hot shortness. (a) Longitudinal section of weld; the dotted line indicated how the sample was sectioned for microexamination. Approximately 2 1 2 ×. (b) Micrograph of section from weld. Hot shortness resulted More

Fig. 16 Pitting on the outside surface of type 316 stainless steel tubes, with downward propagation. Source: Ref 20 More

Fig. 24 Crevice corrosion pitting that has taken place where type 316 bubble caps contact a type 316 stainless steel tray deck. The oxygen-concentration cell corrosion occurred in concentrated acetic acid with minimal oxidizing capacity. 1 8 actual size More

Fig. 15 Surface of a fracture in type 316 stainless steel resulting from SCC by exposure to a boiling solution of 42 wt% MgCl 2 . The fracture in general exhibited the fan-shaped or feather-shaped transgranular cleavage features shown in (a). In a hasty scrutiny, the presence of local areas More

Fig. 27 AISI type 316 stainless steel piping that failed by SCC at welds. Cracking was caused by exposure to condensate containing chlorides leached from insulation. (a) View of piping assembly showing cracks on inner surface of cone. Dimensions given in inches. (b) Macrograph of an unetched More

Fig. 29 Pitting and stress corrosion in type 316 stainless steel evaporator tubes. (a) Rust-stained and pitted area near the top of the evaporator tube. Not clear in the photograph, but visually discernible, are myriads of fine, irregular cracks. (b) Same area shown in (a) but after dye More