Abstract:
Welded ferritic stainless steel tubing having high resistance to hydrogen embrittlement particularly adapted for use in heat exchangers handling chemical media containing hydrogen sulfide or nascent hydrogen and in cathodically protected heat exchangers. The ferritic stainless steel of the welded tubing consists essentially of, in weight percent, carbon at least 0.002, nitrogen at least 0.002, carbon plus nitrogen 0.02 max. and preferably 0.01 to 0.02, chromium 23 to 28, preferably 25 to 28, manganese up to 1, preferably up to 0.5, nickel 1 to 4, silicon up to 1, preferably up to 0.5, phosphorus up to 0.04, sulfur up to 0.02, preferably up to 0.005, molybdenum 2 to 5, preferably 2 to 4, aluminum up to 0.1, columbium 0.60 max. with columbium being at least equal to eight times carbon plus nitrogen, and the balance iron and incidental impurities.

Description:
BACKGROUND OF THE INVENTION 
     1. Field of the Invention 
     The invention relates to welded tubing of a highly corrosion resistant ferritic stainless steel characterized by high resistance to hydrogen embrittlement. The tubing is adapted for use in heat exchangers handling process media containing hydrogen sulfide and other sources of nascent hydrogen, in cathodically protected heat exchangers, and in particular for cathodically protected heat exchangers operated at electrochemical potentials more negative than about -800 millivolts with respect to the saturated calomel reference electrode (SCE). 
     2. Description of the Prior Art 
     Heat exchangers and condensers are devices used to transfer heat from one medium to another. In the shell and tube type heat exchangers hot liquid or vapor is contained in the shell while the cool liquid passes through the tubes. For reasons of performance and economy, many electrical power plant condensers and chemical and petrochemical plant heat exchangers are now built with highly alloyed ferritic stainless steel tubing and with dissimilar metal tubesheets and water boxes. This practice is particularly common in rebuilt condensers or heat exchangers in which ferritic stainless steel tubing has been used to replace copper alloy tubing installed in tubesheets of matching or nearly matching compositions. Condensers and heat exchangers of this conventional construction are well known in the art as described in the following articles: 
     R. O. Miller and H. G. Seip, &#34;Condensers and Heat Exchangers,&#34; Corrosion in Power Generating Equipment, Plenum Plublishing Corporation, 1984. 
     G. V. Spires, et al, &#34;Case History: Lining Condenser Components in a Nuclear Plant,&#34; Journal of Protective Coatings and Linings, 34-41, September 1984. 
     In an apparatus of this type where brackish or seawater cooling are used, the ferritic stainless steel tubing is required to be resistant on one surface to pitting and crevice corrosion as well as other forms of corrosive attack in these aggressive cooling waters and on the other surface to similar forms of corrosive attack from the process media. Since welding is used in either the construction or installation or both with respect to such tubing, the tubing must exhibit good weldability and be resistant to corrosion in the as-welded, and welded and annealed conditions. Also, the toughness and ductility of the tubing in these metallurgical conditions must be sufficient to avoid cracking during the expansion of the tubing into the tubesheets and in other forming operations. 
     For these applications, it is known to use ferritic stainless steels containing about 20 to 30% chromium and which are stabilized by the use of titanium, columbium, zirconium, and aluminum or combinations thereof. These stabilizing elements have generally been deemed to be equivalent for this purpose. 
     A significant disadvantage of welded tubing made from these conventional ferritic stainless steels is the susceptibility of the tubing to hydrogen embrittlement. This embrittlement, coupled with applied or residual stresses, can result in extensive cracking of the tubing. Hydrogen embrittlement has been found to be more pronounced in typical applications where the tubing is exposed to hydrogen sulfide or nascent hydrogen in the media being processed or where the heat exchangers are subjected to cathodic protection to minimize galvanic or crevice corrosion of the tubesheet or water box materials. As indicated in NACE Standard RP-01-69, it is conventional practice when cathodically protecting carbon steel or cast iron components in seawater cooled heat exchangers to utilize electrochemical potentials more electronegative than about -850 millivolts (SCE), whether the protection is afforded by use of sacrifical anodes or by automatic electrical systems. There is a need, therefore, for welded ferritic stainless steel tubing that exhibits high resistance to hydrogen embrittlement when exposed to process media containing hydrogen sulfide or other sources of nascent hydrogen or when used in a cathodically protected heat exchanger or condenser using brackish or seawater cooling. 
     SUMMARY OF THE INVENTION 
     It is accordingly a primary object of the present invention to provide welded tubing of a highly corrosion resistant ferritic stainless steel having high resistance to hydrogen embrittlement and when used in a heat exchanger having media containing hydrogen sulfide or nascent hydrogen, or in cathodically protected heat exchangers, particularly one operated at electrochemical potentials more negative than about -800 millivolts (SCE). 
     In accordance with the invention, it has been determined that welded tubing of corrosion-resistant ferritic stainless steel may satisfy the aforementioned object of the invention with a composition having lower than conventional carbon and nitrogen contents in combination with columbium stabilization and the exclusion of stabilization with titanium, combinations of titanium and columbium, zirconium or aluminum. It is also necessary that the steel contain chromium, molybdenum and nickel, with nickel and molybdenum being in amounts different from those conventionally employed in ferritic stainless steels of this type. 
     The welded tubing in accordance with the invention is of a ferritic stainless steel of a composition, in weight percent, carbon at least 0.002, nitrogen at least 0.002, carbon plus nitrogen 0.02 max. and preferably 0.01 to 0.02, chromium 23 to 28, preferably 25 to 28, manganese up to 1, preferably up to 0.5, nickel 1 to 4, silicon up to 1, preferably up to 0.5, phosphorus up to 0.04, sulfur up to 0.02, preferably up to 0.005, molybdenum 2 to 5, preferably 2 to 4, aluminum up to 0.1, columbium 0.60 max. with columbium being at least equal to eight times carbon plus nitrogen, and the balance iron and incidental impurities. 
     The welded tubing may be made by conventional autogenous welding practices wherein a continuous band of the ferritic stainless steel of a chemical composition in accordance with the invention is roll formed and autogenous welded longitudinally in a continuous fashion to produce the tubing. Conventional practices, such as tungsten-inert gas welding may be used for this purpose. For purposes of the invention and as used herein, the term &#34;welded tubing&#34; includes non-cylindrical shapes or hollows such as used in plate-type heat exchangers. 
     Carbon and nitrogen contents as low as about 0.002% each may be obtained by vacuum induction or electron-beam melting practices; whereas, carbon plus nitrogen contents as low as about 0.01% may be obtained by conventional large capacity vacuum-oxygen refining practices. As will be demonstrated by the data presented herein, the invention finds utility with welded tubing made from ferritic stainless steel melted in accordance with either of these practices and having carbon and nitrogen contents each at a minimum of 0.002% or a combined minimum of 0.01% to a maximum of 0.02%. As will be demonstrated by the data presented herein, it is not only required that stabilization be effected only by the use of columbium, but carbon and nitrogen in combination must also be closely controlled in accordance with the limits set forth herein. 
     Manganese is an austenite forming element and also a potent solid solution strengthening element in ferritic stainless steels. Accordingly, in accordance with the invention, manganese must be maintained below about 1% and preferably below about 0.5%. Sulfur is a common residual element in ferritic stainless steels and must be controlled to a maximum of 0.02%, and preferably below 0.005%, to avoid hot cracking and permit effective welding. Silicon improves welding from the standpoint of producing the desired fluidity in the alloy, but it is a strong solid solution strengthening element and thus must be kept below about 1%, and preferably below about 0.5%. Although nickel is a strong austenite forming element it must be present for purposes of improved weld toughness and ductility. Chromium is essential for corrosion resistance, particularly resistance to pitting and crevice corrosion in seawater and other chloride containing environments. Chromium within the limits of the invention provides the desired corrosion resistance, but higher chromium content impairs weld toughness. Molybdenum is necessary for providing the required corrosion resistance; however, if molybdenum is present in excessive amounts it introduces undesirable second phases which reduce toughness and corrosion resistance. Aluminum is an effective deoxidizing element required during the refining operation, but excessive aluminum results in problems during welding. 
     Columbium, as discussed, is needed to prevent weld intergranular corrosion. Excessive columbium, however, adversely affects weld toughness. 
    
    
     DETAILED DESCRIPTION OF THE PREFERRED EMBODIMENTS 
     Reference will now be made in detail to presently preferred embodiments of the invention, examples of which are described below. 
     Two groups of tests were conducted to evaluate the ferritic stainless steels listed in Table I with respect to properties essential to their use in brackish or seawater cooled heat exchangers and power plant condensers. One group of tests was conducted to compare the resistance of these materials to intergranular and pitting corrosion and their formability in the non-welded and welded conditions. The other group of tests was conducted to evaluate the susceptibility of the materials to hydrogen embrittlement. 
     Corrosion Resistance and Mechanical Properties 
     Two ASTM tests were used to compare the intergranular corrosion resistance of the ferritic stainless steel tubing of the invention in the as-welded condition to that of other ferritic stainless steels listed in Table I. The copper-copper sulfate-sulfuric acid test (ASTM A763, Practice Y) was used to evaluate susceptibility to intergranular corrosion associated with the precipitation of chromium carbides and/or nitrides. The ferric sulfate-sulfuric acid test (ASTM A763, Practice X) was used to evaluate susceptibility to intergranular corrosion associated with the precipitation of chromium carbides and/or nitrides and with the precipitation of chi, sigma, and other intermetallic phases. The results of the copper-copper sulfate-sulfuric acid tests on four alloys of varying columbium and molybdenum content are given in Table II. They clearly show that Alloy 37, having a base composition within the scope of invention but which contains no columbium, is susceptible to intergranular attack in the as-welded condition. The welds of the three other alloys evaluated (Alloys 15, 20, and 19) which contain an amount of columbium in excess of eight times their carbon plus nitrogen content, are resistant to intergranular attack in this solution. The results of the ferric sulfate-sulfuric acid tests are given in Table III for five alloys of different columbium and molbydenum contents. Similar to the results obtained in the copper-copper sulfate-sulfuric acid test, the results of these tests show that Alloy 37, having a base composition within the scope of the invention but which contains no columbium, is susceptible to intergranular corrosion in the as-welded condition. However, they also show that Alloy 19, which contains 4.44% molybdenum, and Alloy 18, which contains 5.34% molybdenum, are susceptible to intergranular corrosion in this test. Thus, in the ferric sulfate-sulfuric acid test, which is representative of highly oxidizing chemical media, both columbium and molybdenum contents need to be controlled to avoid intergranular corrosion. Columbium-stabilized tubing of the invention having less than about 4.00% molybdenum are resistant to intergranular corrosion in both the copper-copper sulfate-sulfuric and ferric sulfate-sulfuric acid tests, and therefore have the widest practical application. The as-welded columbium-stabilized tubing of the invention containing more than about 4.00% molybdenum is not resistant to integranular attack in the ferric sulfate-sulfuric acid test, and therefore its use is limited in highly oxidizing chemical media. 
     The molybdenum content of the stainless steel tubing of the invention is also important with respect to its pitting resistance when used in heat exchangers utilizing brackish or seawater cooling. To demonstrate this, a series of tests were conducted on several of the alloys listed in Table I to compare their resistance to pitting at different temperatures in a neutral solution of substitute seawater containing 10 g/liter of potassium ferricyanide to increase its corrosivity. The results of these tests are given in Table IV. They show that the temperature needed to initiate pitting in these alloys increases with molybdenum content. More importantly, they show that to obtain good pitting resistance at the elevated temperatures commonly encountered in many heat exchanger applications (60° C.), the tubing of the invention must contain at least about 2% molybdenum, as demonstrated by the relative performance of Alloy 13 which contains 1.8% molybdenum and Alloy 14 which contains 2.69% molybdenum. Alloy 15, which is stabilized with columbium and which contains 3.51% molybdenum, was immune to pitting in these tests. 
     The weld ductility of several of the alloys listed in Table I were compared by making Olsen cup tests on 0.037-inch thick TIG welds and by comparing the results to those obtained from similar tests made on the annealed and unwelded base materials. The results are given in Table V. They show that the Olsen cup ductility of Alloy 7 which contains 0.41% nickel is significantly reduced by welding. In comparison, the Olsen cup ductility of the alloys containing more than about 1.0% nickel, and less than about 5.0% molybdenum as with Alloys 10, 8, 15, and 19, is as good in the as-welded condition as in the unwelded condition. Thus, for heat exchanger applications, in which the tubes are bent or mechanically expanded during installation, the nickel-bearing materials of the invention have substantial practical advantages. It is necesary, however, to restrict the molybdenum content of the nickel-bearing alloys of the invention to less than about 5% because of the formation of brittle second phases which, as shown by the performance of Alloy 18, severely reduce Olsen cup ductility in both the unwelded and welded conditions. 
     Hydrogen Embrittlement 
     Three basic methods were used to charge the test steels with hydrogen and to evaluate their susceptibilty to hydrogen embrittlement. One method involved charging materials in substitute or natural seawater for different times at various electrochemical potentials analogous to those used for cathodic protection in condensers and heat exchangers. The second method involved charging samples in a solution containing 50% hydrochloric acid (36.5 to 38.0% HCl) and 50% water by volume to which 20 gram/liter of selenium dioxide was added to promote hydrogen absorption. With these two charging practices, the susceptibility of the steels to hydrogen embrittlement was evaluated according to the ability of a sample to withstand a 180-degree bend without cracking or fissuring. The specimens withstanding a 180-degree bend without completely fracturing were considered to be highly resistant to embrittlement while those that cracked or fissured upon bending to 180° were considered to be susceptible to hydrogen embrittlement. The third method consisted of testing samples stressed in tension as three-point bent beams according to NACE Test Method 01-77 in an aqueous solution containing 5% sodium chloride and 0.5% acetic acid at ambient temperature. The test solution was deaerated for two hours with nitrogen prior to the introduction of hydrogen sulfide gas which was continuously bubbled into the test solution throughout the duration of the 30-day (720 hours) test period. Specimens that did not crack during the 30-day test period were considered to have passed the test. 
     Three series of electrochemical tests were conducted to compare the hydrogen embrittlement resistance of the ferritic stainless steel tubing of the invention to that of the other corrosion resistant ferritic stainless steels listed in Table I. In the initial series of tests, samples of a titanium-stabilized highly corrosion resistant ferritic stainless steel currently used in seawater cooled condensers (Alloy 9) and of a ferritic stainless steel within the scope of the invention (Alloy 15) were charged in aerated substitute seawater (ASTM D-1141-52, Formula A) at 45° C. to establish the time required at various electrochemical potentials to produce hydrogen embrittlement, as measured by a loss in bend ductility. 
     The results of these tests, which are given in Table VI, show that at electrochemical potentials between -700 and -800 millivolts with respect to the standard calomel electrode (SCE) essentially no embrittlement occurs with Alloy 9 for exposure times up to 100 hours. However, as the applied electrochemical potential becomes more negative than -800 millivolts (SCE), the samples of Alloy 9 become increasingly susceptible to hydrogen embrittlement, as indicated by the shorter exposure times needed to produce a loss of bend ductility. Thus, the data show that a titanium-stabilized highly corrosion resistant ferritic stainless steel of conventional composition becomes susceptible to hydrogen embrittlement at electrochemical potentials more negative than -800 millivolts (SCE). None of the samples from Alloy 15 whose composition is within the scope of the invention, showed any signs of hydrogen embrittlement when tested under several of the same test conditions. 
     Based on the data in Table VI, a simplified screening test was devised to further compare the resistance of the ferritic stainless steels listed in Table I to hydrogen embrittlement. The test involved measuring the bend ductility of specimens exposed for 24 hours at potentials of -1000 and/or -1200 millivolts (SCE), conditions which as indicated in Table VI embrittle a titanium-stabilized highly alloyed ferritic stainless steel of conventional composition. 
     As shown by the data in Table VII, only Alloy 15 which contains 0.012% carbon plus nitrogen and 0.26% columbium and Alloy 17 which contains 0.016% carbon plus nitrogen and 0.27% columbium were resistant to hydrogen embrittlement in these tests. All other alloys of similiar base composition, including Alloy 1 which contains 0.01% carbon plus nitrogen and 0.34% titanium; Alloy 30 which contains 0.020% carbon plus nitrogen, 0.16% titanium, and 0.14% columbium; and Alloy 21 which contains 0.022% carbon plus nitrogen and 0.33% columbium were susceptible to hydrogen embrittlement in this test. Thus, in accordance with this invention, the data show that a marked improvement in the resistance to hydrogen embrittlement can be obtained by lowering carbon plus nitrogen to below about 0.02% and by using columbium rather than titanium or a mixture of titanium and columbium for stabilization. 
     To further demonstrate the advantage of the ferritic stainless steel tubing of the invention, samples of Alloy 1 which contains 0.01% carbon plus nitrogen and 0.34% titanium; Alloy 9 which contains 0.038% carbon plus nitrogen and 0.50% titanium; and of Alloy 15 which contains 0.012% carbon plus nitrogen and 0.26% columbium were exposed for various lengths of time at different electrochemical potentials in natural flowing seawater at ambient temperature. 
     After being exposed at the potentials and times indicated in Table VIII, the samples were removed from the test and quickly bent 180° to determine whether they were susceptible to hydrogen embrittlement. Of the three alloys tested, only Alloy 15 was resistant to hydrogen embrittlement. Thus, the results of these tests again show that lowering carbon plus nitrogen to below about 0.02% and by using columbium rather than titanium for stabilization, as with Alloy 15, results in a substantial improvement in the resistance of highly alloyed ferritic stainless steels to hydrogen embrittlement. 
     Samples of the alloys listed in Table I were also compared for their susceptibility to hydrogen embrittlement by conducting bend tests on specimens which were charged for 40 minutes in a solution containing 50% hydrochloric acid (36.5 to 38.0% HCl) and 50% water by volume to which 20 gram/liter of selenium dioxide was added to promote hydrogen absorption. 
     The results of these tests are given in Table IX. Similar to the results presented earlier for the electrochemical tests, the only alloys (15, 16, 17, 20) that were resistant to hydrogen embrittlement in this test were the columbium-stabilized alloys containing less than about 0.02% carbon plus nitrogen. All the other alloys evaluated including columbium-stabilized alloys containing more than about 0.020% carbon plus nitrogen (Alloys 21 and 22), titanium-stabilized alloys containing as little as 0.010 carbon plus nitrogen (Alloy 1), and alloys stabilized with both columbium and titanium and containing 0.020% carbon plus nitrogen were susceptible to hydrogen embrittlement in these tests. Titanium-stabilized alloys with chromium and molybdenum contents insufficient for use in seawater (Alloys 12) or sufficient for use in seawater (Alloy 7) were also subject to embrittlement in these tests. Thus, these results again demonstrate that for highly corrosion resistant ferritic stainless steels improved resistance to hydrogen embrittlement can be obtained only by lowering carbon plus nitrogen content to below about 0.02% and using columbium for stabilization rather than titanium alone, or mixtures of columbium, titanium or aluminum. 
     One additional series of chemical charging tests were conducted on samples of Alloy 15 and Alloy 9 in the as-annealed, as-welded, and welded and annealed conditions to determine the effect of TIG welding on their resistance to hydrogen embrittlement. The results of these tests, which are given in Table X, show that welding does not significantly change the resistance of these alloys to hydrogen-embrittlement. Alloy 15, having a composition within the scope of the invention, remains resistant to hydrogen embrittlement after welding; whereas Alloy 9 with a composition outside the claims of the invention remains susceptible to hydrogen embrittlement after welding. 
     The results of the three-point bend beam tests conducted according to NACE Test Method 01-77 on a conventional titanium-stabilized ferritic stainless steel (Alloy 11) and on a columbium-stabilized ferritic stainless steel (Alloy 15) having a composition within the scope of the invention are given in Table XI. Here, it can be seen that Alloy 15 is totally resistant to cracking when stressed in tension up to 75 ksi; whereas, Alloy 11 having a composition outside the claims of the invention fails when stressed to as little as 15 ksi in tension. Thus, the results show that in hydrogen sulfide containing environments, the resistance of highly corrosion resistant ferritic stainless steels to hydrogen embrittlement in such environment can be markedly improved by using columbium stabilization and by controlling carbon and nitrogen within the limits of the invention. 
     As may be seen from the above test results maintaining carbon plus nitrogen within the limits of the invention or stabilizing by the use of columbium alone in accordance with the invention will not achieve the desired resistance to hydrogen embrittlement. It is necessary that control of carbon plus nitrogen within the limits of the invention in combination with columbium stabilization be used. 
     
                                           TABLE I__________________________________________________________________________Chemical Composition of Experimental MaterialsMaterialC  N  Mn P  S  Si                 Ni Cr Mo Ti                            Cb                              Cu Al C + N__________________________________________________________________________Alloys Titanium Stabilized1    .002   .008      .16         .024            .003               .25                 1.85                    26.92                       3.34                          .34                            --                              .005                                 .005                                    .0102    .009   .015      .73         .016            .006               .42                 2.25                    26.95                       3.67                          .43                            --                              .11                                 .02                                    .0243    .019   .008      .24         .016            .005               .29                 2.01                    27.85                       3.37                          .30                            --                              -- .05                                    .0274    .014   .016      .12         .020            .030               .25                 0.25                    25.61                       0.95                          .49                            --                              .04                                 .02                                    .0305    .010   .023      .70         .017            .006               .45                 1.98                    27.00                       3.56                          .42                            --                              .12                                 .05                                    .0336    .019   .014      .38      .32                 4.10                    24.54                       3.89                          .41                            --      .0337    .016   .020      .29         .027            .002               .18                 0.41                    28.32                       3.68                          .68                            --   .07                                    .0368    .015   .022      .35         .021            .004               .20                 2.06                    27.16                       3.36                          .54                            --                              .15                                 .08                                    .0379    .018   .020      .30         .024            .002               .21                 1.88                    27.30                       3.42                          .50                            --      .03810   .029   .012      .31         .027            .001               .41                 1.26                    27.05                       3.39                          .45                            --                              .12                                 .07                                    .04111   .018   .025      .26         .021            .001               .40                 1.99                    27.00                       3.40                          .44                            --                              -- -- .04312   .018   .029      .28         .017            -- .38                 0.23                    25.91                       0.98                          .56                            --                              .13                                 .05                                    .04713   .021   .026      .28         .020            .013               .55                 0.22                    26.09                       1.81                          .45                            --                              .12                                 -- .04714   .024   .029      .29         .023            -- .46                 0.21                    25.63                       2.69                          .41                            --                              .13                                 .04                                    .053Alloys Columbium Stabilized15   .006   .006      .36         .025            .001               .33                 1.92                    26.90                       3.51                          --                            .26                              .06                                 .09                                    .01216   .006   .006      .25         .020            .003               .28                 1.98                    27.64                       3.48                          --                            .48  .05                                    .01217   .009   .007      .20         .020            .005               .26                 2.03                    27.70                       3.51                          --                            .27  .09                                    .01618   .007   .008      .20         .010            .005               .25                 2.02                    27.18                       5.34                          --                            .37                              -- .05                                    .01519   .009   .008      .25         .020            .003               .26                 2.02                    27.32                       4.44                          --                            .37                              -- .06                                    .01720   .010   .009      .21         .020            .006               .27                 1.97                    27.39                       3.50                          --                            .36  .10                                    .01921   .014   .008      .25         .020            .005               .25                 2.06                    27.81                       3.53                          --                            .33  .08                                    .02222   .015   .009      .21         .020            .005               .25                 2.04                    27.68                       3.47                          --                            .32  .07                                    .02423   .013   .015      .24         .016            .004               .26                 2.00                    28.13                       3.48                          --                            .46  .02                                    .02824   .009   .019      .25         .015            .006               .25                 2.00                    27.51                       3.49                          --                            .47  .02                                    .02825   .018   .014      .25         .018            .006               .29                 2.00                    27.90                       3.40                          --                            .34  .04                                    .03226   .020   .017      .26         .020            .004               .28                 2.05                    27.37                       3.52                          --                            .32  .23                                    .03727   .027   .018      .23         .015            .003               .25                 1.99                    27.90                       3.50                          --                            .46  .01                                    .04528   .021   .025      .22         .020            .004               .26                 2.03                    27.84                       3.50                          --                            .33  .09                                    .04629   .029   .035      .23         .016            .003               .24                 1.99                    28.00                       3.50                          --                            .47  .04                                    .064Alloys Titanium and Columbium Stabilized30   .014   .006      .23         .022            .006               .29                 2.04                    27.80                       3.41                          .16                            .14  .05                                    .02031   .027   .024      .37         .032            .005               .46                 2.03                    27.30                       3.49                          .29                            .44  .02                                    .05132   .029   .022      .38         .033            .005               .47                 2.03                    27.29                       3.49                          .12                            .44  .04                                    .05132   .029   .022      .38         .033            .005               .47                 2.03                    27.29                       3.49                          .12                            .44  .04                                    .05133   .027   .025      .36         .033            .005               .43                 2.03                    27.40                       3.49                          .20                            .43  .04                                    .05234   .002   .032      .28         .023            .001               .33                 0.27                    28.65                       3.79                          .33                            .17     .05435   .030   .028      .23         .015            .003               .25                 1.99                    27.80                       3.50                          .27                            .27  .03                                    .058Alloys Not Stabilized36   .003   .010      -- .010            .007               .27                 0.17                    26.99                       0.97                          --                            --                              .01                                 -- .01337   .008   .007      .19         .020            .005               .26                 2.02                    27.72                       3.55                          --                            --                              -- .05                                    .015__________________________________________________________________________ 
    
     
                       TABLE II______________________________________Intergranular Corrosion Resistance of Welded Alloys in theCopper-Copper Sulfate-Sulfuric Acid (ASTM A763,Practice Y) Test.sup.(a)             Grain Drop Out SeverityMaterial  C + N   Cr     Mo   Cb   Base Weld   HAZ.sup.(b)______________________________________37     0.015   27.27  3.55 --   none moderate                                       moderate15     0.012   26.90  3.51 0.26 none none   none20     0.019   27.39  3.50 0.36 none none   none19     0.017   27.32  4.50 0.37 none none   none______________________________________ .sup.(a) Samples TIG welded without filler metal at a thickness of 0.037 inch .sup.(b) HAZ -- heat affected zone 
    
     
                       TABLE III______________________________________Intergranular Corrosion Resistance of Welded Alloys in theFerric Sulfate-Sulfuric Acid (ASTM A763, Practice X) Test.sup.(a)             Grain Drop Out SeverityMaterial  C + N   Cr     Mo   Cb   Base  Weld  HAZ.sup.(b)______________________________________37     0.015   27.27  3.55 --   none  light moderate15     0.012   26.90  3.51 0.26 none  none  none20     0.019   27.39  3.50 0.36 none  none  none19     0.017   27.32  4.44 0.37 none  none  light18     0.016   27.18  5.34 0.37 none  light light______________________________________ .sup.(a) Samples TIG welded without filler metal at a thickness of 0.037 inch .sup.(b) HAZ -- heat affected zone 
    
     
                       TABLE IV______________________________________Pitting Resistance of Various Alloys in Neutral SubstituteSeawater Containing 10 gram/liter of Potassium Ferricyanide.sup.(a)Mater- C +                       Severity of Pittingial   N      Cr     Ni   Mo   Ti   Cb   40° C.                                         60° C.______________________________________36    0.013  26.99  0.17 0.97 --   --   none  moderate12    0.047  25.61  0.23 0.99 0.56 --   none  moderate13    0.047  26.09  0.22 1.81 0.45 --   none  light14    0.053  25.63  0.21 2.69 0.41 --   none  none15    0.012  26.90  1.92 3.51 --   0.26 none  none19    0.017  27.32  2.02 4.44 --   0.37 none  none______________________________________ .sup.(a) Tests conducted for 24 hours in neutral substitute seawater containing 10 gram/liter K.sub.3 Fe(CN).sub.6 
    
     
                                           TABLE V__________________________________________________________________________Effect of Nickel Content on the Olsen Cup Ductility ofVarious Unwelded and TIG-Welded Ferritic Stainless Steels.sup.(a)                    Olsen Cup Height in..sup.(b)MaterialC + N    Cr  Ni Mo Ti Cb Unwelded                           As-welded__________________________________________________________________________7    0.036    28.32        0.41           3.65              0.68                 -- 0.306  0.14310   0.041    27.05        1.26           3.39              0.45                 -- 0.336  0.3478    0.037    27.16        2.06           3.36              0.54                 -- 0.298  0.30115   0.012    26.90        1.92           3.51              -- 0.26                    0.340  0.34019   0.017    27.32        2.02           4.44              -- 0.37                    0.317  0.33818   0.016    27.18        2.20           5.34              -- 0.37                    0.205  0.115__________________________________________________________________________ .sup.(a) Samples TIGwelded wihtout filler metal at a thickness of 0.037 inch .sup.(b) Maximum cup height without failure 
    
     
                       TABLE VI______________________________________Effect of Cathodic Charging Potential and Time on the BendDuctility (Embrittlement) of Alloy 9 in Substitute SeawaterPotential(Millivolts   Charging Time (Hours)vs. SCE)   1     1.5   2   3   5   16  48  68  100  120  750______________________________________700     P.sup.a         --    --  --  P   --  P   P   --   P    P800     P     --    --  --  --  P   --  P   P    --850     P     --    --  --  P   F   --  F   --   --   --900     P     --    --  --  F   F   --  --  --   --   --1000    P     P     P   F   --  F   --  --  --   --   --1100    P     F     --1200    F     F     --1400    F     F     --______________________________________ .sup.a P  pass 180° bend test, F  failed 180° bend test 
    
     
                                           TABLE VII__________________________________________________________________________Embrittlement of Samples Charged for 24 Hours atIndicated Potentials in Substitute Seawater at 45° C. (115°F.).sup.(a)                       Applied Potential                       (Millivolts)Materials C + N     Cr Mo Ni Ti Cb Al -1000                            -1200__________________________________________________________________________1     0.010     26.92        3.34           1.85              0.34                 -- .005                       --   F2     0.024     26.95        3.67           2.25              0.43                 -- .02                       F    F3     0.027     27.85        3.37           2.01              0.30                 -- .05                       F    F6     0.033     24.54        3.89           4.10              0.41                 -- .07                       F    F7     0.036     28.32        3.89           0.41              0.68                 -- -- --   F9     0.038     27.30        3.42           1.88              0.50                 -- -- F    F30    0.020     27.80        3.41           2.04              0.16                 0.14                    0.5                       F    --31    0.051     27.30        3.49           2.03              0.29                 0.44                    .02                       F    --32    0.051     27.29        3.49           2.03              0.12                 0.44                    .04                       --   F34    0.058     28.65        3.79           0.27              0.33                 0.17                    -- F    --15    0.012     26.90        3.51           1.92              -- 0.26                    .09                       P    P17    0.016     27.70        3.51           2.03              -- 0.27                    .09                       P    P20    0.019     27.39        3.50           1.97              -- 0.36                    .10                       P    P21    0.022     27.81        3.53           2.06              -- 0.33                    .08                       --   F22    0.024     27.68        3.47           2.04              -- 0.32                    .07                       F    F25    0.032     27.90        3.40           2.00              -- 0.34                    .04                       --   F28    0.046     27.84        3.50           2.03              -- 0.33                    .09                       --   F__________________________________________________________________________ .sup.(a) Samples bent 180° F. after charging; F -- Failed, P -- Pass 
    
     
                                           TABLE VIII__________________________________________________________________________Embrittlement of Specimens Charged at Indicated ElectrochemicalPotentials in Natural Filtered Flowing Seawater at AmbientTemperature.sup.(a)          Charging Potentials (Millivolts vs. SCE)MaterialC + N    Ti Cb -850   -1000  -1200  -1400 -2000__________________________________________________________________________1    0.010    0.34       -- F (4.7 days)                 F (4.7 days)                        F (4.7 days)                               --    --          --     F (11.6 days)                        F (11.6 days)                               --    --9    0.038    0.50       -- --     F (3 days)                        --     F (3 days)                                     F (3 days)          F (11.6 days)                 F (11.6 days)                        F (11.6 days)                               --    --15   0.012    -- 0.26          --     P (3 days)                        --     P (3 days)                                     P (28 days)          --     P (14 days)                        --     --    P (14 days)          --     P (28 days)                        --     P (28 days)                                     P (28 days)__________________________________________________________________________ .sup.(a) Samples bent 180° F. after indicated exposures; F -- Failed, P -- Pass 
    
     
                       TABLE IX______________________________________Embrittlement of Samples Charged Chemically for 40 Minutes inHydrochloric Acid Test Solution Containing 50% HydrochloricAcid Plus 50% Water to Which 20 g/literSelenium Dioxide Was AddedMater-ial   C + N   Cr     Mo   Ni   Ti   Cb   180° Bend______________________________________                                    Test1     0.010   26.92  3.34 1.85 0.34 --   F (fail)2     0.024   26.95  3.67 2.25 0.43 --   F3     0.027   27.85  3.37 2.01 0.30 --   F4     0.030   25.61  0.95 0.25 0.49 --   F5     0.033   27.00  3.56 1.98 0.42 --   F6     0.033   24.54  3.89 4.10 0.41 --   F7     0.036   28.32  3.89 0.41 0.68 --   F8     0.037   27.16  3.36 2.06 0.54 --   F9     0.038   27.30  3.42 1.88 0.50 --   F10    0.041   27.30  3.42 1.88 0.50 --   F30    0.020   27.80  3.41 2.04 0.16 0.14 F31    0.051   27.30  3.49 2.03 0.29 0.44 F32    0.051   27.29  3.49 2.03 0.12 0.44 F33    0.052   27.40  3.49 2.03 0.20 0.43 F34    0.054   28.65  3.79 0.27 0.33 0.17 F35    0.058   27.80  3.50 1.99 0.27 0.27 F15    0.012   26.90  3.51 1.92 --   0.26 P(pass)16    0.012   27.64  3.48 1.98 --   0.48 P17    0.016   27.70  3.51 2.03 --   0.27 P20    0.019   27.39  3.50 1.97 --   0.36 P21    0.022   27.81  3.53 2.06 --   0.33 F23    0.028   28.13  3.48 2.00 --   0.46 F24    0.028   27.51  3.49 2.00 --   0.47 F25    0.032   27.90  3.40 2.00 --   0.34 F26    0.037   27.37  3.52 2.05 --   0.32 F27    0.045   27.90  3.50 1.99 --   0.46 F28    0.046   27.84  3.50 2.03 --   0.33 F29    0.064   28.00  3.50 1.99 --   0.47 F______________________________________ 
    
     
                                           TABLE X__________________________________________________________________________Embrittlement of Welded Samples Charged Chemically40 Minutes in Hydrochloric Acid Test Solution.sup.(a)MetallurgicalMaterialCondition  C + N               Cr Mo Ni Ti Cb 180° Bend Test__________________________________________________________________________9    Cold Rolled and           0.038               27.30                  3.42                     1.88                        0.50                           -- F (Fail)AnnealedAs-welded                     FWelded and Annealed           F15   Cold Rolled and           0.012               26.90                  3.51                     1.92                        -- 0.26                              P (Pass)AnnealedAs-welded                     PWelded and Annealed           P__________________________________________________________________________ .sup.(a) Tests conducted on coldrolled and annealed 0.037 inch thick stri which was TIGwelded without filler metal 
    
     
                       TABLE XI______________________________________Results of Three-point Bent Beam Tests onAlloys 11 and 15 in the NACE TM-01-77 Test      Stress  Exposure     Microscopic      Level   Time         ExaminationMaterial   (ksi)   (hours)      of Samples______________________________________11         15      720.sup.(1)  Cracks      30      720          No cracks      45      720          Cracks      60      720          Cracks      75      (150)        Broke in test15         15      720          No cracks      30      720          No cracks      45      720          No cracks      60      720          No cracks      75      720          No cracks______________________________________ .sup.(1) Numbers without parenthesis indicate specimens did not fracture, 30 days exposure. Numbers in parenthesis indicate specimen fractured at the approximate time (+/- 50 hours) shown.