Method of detecting the embrittlement of two-phase stainless steel

BACKGROUND OF THE INVENTION
1. Field of the Invention
The present invention relates to a method of detecting the degree of embrittlement of two-phase stainless steel and in particular to a method of detecting the embrittlement, and estimating the degree of embrittlement, of two-phase stainless steel in cooling tubes, pump casings etc. in a pressurized water reactor.
2. Description of the Related Art
For a method of estimating the degree of embrittlement of a member of two-phase stainless steel, there is proposed a formula by which the degree of embrittlement can be estimated from chemical components, operation temperature and operation time. However, there is no method of estimating the degree of embrittlement by examining the state of an actual machine.
There remains anxiety about the reliability of a method based on such formula because an actual machine is not examined to confirm its degree of embrittlement.
SUMMARY OF THE INVENTION
The present invention was made under these circumstances, and the object of the invention is to provide a method of detecting the embrittlement of two-phase stainless steel in which Charpy impact absorption energy can be directly obtained from measurements capable of non-destructive examination, or estimated by examination, based on the mechanism of embrittlement of two-phase stainless steel as well as on the theory of Charpy impact absorption energy of two-phase material.
The first aspect of the present invention relates to a method of detecting the embrittlement of two-phase stainless steel, which comprises measuring the hardness of the ferrite phase (.alpha.-phase), and the hardness of the austenite phase (.gamma.-phase) of two-phase stainless steel, along with reading the area ratio of the ferrite phase from microstructure observation to estimate the Charpy impact absorption energy at room temperature of the two-phase stainless steel from the above specified 3 values.
The second aspect of the present invention relates to a method of detecting the embrittlement of two-phase stainless steel, which comprises measuring the hardness of the ferrite phase, and the hardness of the austenite phase of two-phase stainless steel, along with reading the area ratio of the ferrite phase and the space between the ferrite phases from microstructure observation to estimate the Charpy impact absorption energy at room temperature of the two-phase stainless steel from the above specified 4 values.
The third aspect of the present invention relates to a method of detecting the embrittlement of two-phase stainless steel, which comprises measuring the hardness of the ferrite phase, and the hardness of the austenite phase of two-phase stainless steel, along with reading the area ratio of the ferrite phase, the space between the ferrite phases, and the occupying ratio of carbide in the grain boundary length from microstructure observation to estimate the Charpy impact absorption energy at room temperature of the two-phase stainless steel from the above specified 5 values.
DETAILED DESCRIPTION OF THE INVENTION
The first aspect of the present invention is described below in detail.
Measurements capable of non-destructive examination includes hardness of ferrite phase, H.sub.V F, hardness of austenite phase, H.sub.V A, and area ratio of ferrite phase, FN.
The Charpy impact absorption energy, C.sub.V, of two-phase stainless steel may be expressed as follows:
C.sub.V =g.times.{AF/100).times.C.sub.V F+(AA/100).times.C.sub.V A}. . . (1)
where AF and AA are the area ratios of ferrite and austenite phases respectively on a fracture of a test specimen after testing; g is a coefficient of correction; AF+AA=100; C.sub.V F is the absorption energy of ferrite phase.
In equation (1), AF+AA=100 where C.sub.V F is the absorption energy of ferrite phase; and C.sub.V A is the absorption energy of austenite phase.
To become hard with embrittlement is a general characteristic of a material. Hence, we think that C.sub.V F and C.sub.V A can be estimated from the hardness H.sub.V F and H.sub.V A of the respective phases. It is assumed that they can be expressed in e.g. the following equations (2) and (3):
C.sub.V F=bF.times.H.sub.V F+aF . . . (2)
C.sub.V A=ba.times.H.sub.V A+aA . . . (3)
It is further assumed that the area ratio AA of the austenite phase expressed in terms of the area ratio AF of the ferrite phase (or 100-AF) on a fracture can be expressed by the area ratio FN of the ferrite phase. For example, it can be assumed that AA can be expressed by the following equation (4):
AA/100=dF.times.FN/100+cF(=1-AF/100) . . . (4)
If the above assumptions can hold, Charpy impact absorption energy can be estimated from H.sub.V F, H.sub.V A and FN by the above equation (1). That is, degree of embrittlement (usually estimated by a decrease in absorption energy etc.) can be estimated by non-destructive examination.
Hence, two-phase stainless steel having various degrees of embrittlement is prepared and determined for Experimental C.sub.V (experimental value of absorption energy), H.sub.V F, H.sub.V A, AF (AA) and FN, to formulate an optimum estimation equation.
The optimum estimation equation refers to an equation where I.sub.error expressed by the following equation (5) reaches minimum: ##EQU1## where Estimated C.sub.V is estimated absorption energy; Experimental C.sub.V is experimental absorption energy; and i means each test material.
The estimation equation thus obtained is as shown in the following equation (6) where Charpy impact absorption energy is expressed in terms of 3 examinable values, H.sub.V F, H.sub.V A and FN.
Estimated C.sub.V =g.times.{dF.times.FN/100+cF)(bA.times.H.sub.V A+aA) +(1-dF.times.FN/100-cf) (bF.times.H.sub.V F+aF)} . . . (6)
where g is a coefficient of correction.
The Charpy impact absorption energy of an actual machine can be obtained from non-destructively examinable and obtainable measurements from the actual machine, i.e. hardness of ferrite phase H.sub.V F, hardness of austenite phase H.sub.V A, and area ratio of ferrite phase, FN. A decrease in absorption energy indicates embrittlement and can thus serves as an indicator of degree of embrittlement.
According to the first aspect of the present invention, there can be provided a method of detecting the embrittlement of two-phase stainless steel in which Charpy impact absorption energy can be directly obtained from measurements capable of non-destructive examination, or estimated by examination, based on the mechanism of embrittlement of two-phase stainless steel as well as on the theory of Charpy impact absorption energy of two-phase material.
In the first aspect of the present invention, the Charpy impact absorption energy at room temperature of two-phase stainless steel is estimated from 3 values obtained by measuring the hardness of the ferrite phase, H.sub.V F, and the hardness of the austenite phase, H.sub.V A, of two-phase stainless steel along with reading the area ratio of the ferrite phase from microstructure observation to estimate the embrittlement of of a member of two-phase stainless steel, but there is a scattering of .+-.70 J. According to the second aspect of the present invention, the improvement of estimation accuracy (.+-.20 J) can be achieved by adding the space between the ferrite phases, FS, as estimation information.
The second aspect of the present invention is a method of detecting the embrittlement of two-phase stainless steel, which comprises measuring the hardness of the ferrite phase and the hardness of the austenite phase of two-phase stainless steel, along with reading the area ratio of the ferrite phase and the space between the ferrite phases from microstructure observation to estimate the Charpy impact absorption energy at room temperature of the two-phase stainless steel from the above specified 4 values.
The second aspect of the present invention is described below in detail.
Measurements capable of non-destructive examination includes hardness of ferrite phase, H.sub.V F, hardness of austenite phase, H.sub.V A, area ratio of ferrite phase, FN, and space between ferrite phases, FS.
The Charpy impact absorption energy of two-phase stainless steel, C.sub.V, may be expressed in the following formula (7) assuming that 100-AA is the area ratio of the ferrite phase, and AA is the area ratio of the austenite phase, on a fracture of a test specimen after testing:
C.sub.V =g.times.{(1-AA/100).times.C.sub.V F +(AA/100.times.C.sub.V A)}. . . (7)
where C.sub.V F is the absorption energy of the ferrite phase; C.sub.V A is the absorption energy of the austenite phase; and g is a coefficient of correction.
To become hard with embrittlement is a general characteristic of a material. Combining this with the fact shown in FIG. 5 that is discussed later, we think that C.sub.V F and C.sub.V A can be estimated from the hardness H.sub.V F and H.sub.V A of the respective phases. It is assumed that they can be expressed in the following equations (8) and (9):
C.sub.V F=aF+bF.times.H.sub.V F . . . (8)
C.sub.V A=aA+bA.times.H.sub.V A . . . (9)
where aF, bF, aA and bF are constants.
It is further assumed that the area AA of the austenite phase on a fracture of a test specimen after testing can be expressed in terms of the area ratio FN, or 1-FN, of the ferrite phase on microstructure by e.g. the following equation (10):
1-AA/100=cF+dF.times.FN/100 . . . (10)
where cF and dF are constants.
If the above assumptions can hold, Charpy impact absorption energy at room temperature can be estimated from H.sub.V F, H.sub.V A and FN. That is, degree of embrittlement (usually estimated by a decrease in absorption energy etc.) can be estimated by non-destructive examination.
However, the space between the ferrite phases may not be identical even if the ferrite phase is present in the same amount of FN as microstructure. The space between the ferrite phases, FS, are automatically determined in 3 divided lines at the X-axis side and 4 divided lines at the Y-axis side in an image-processing unit by incorporation of a few microphotographs. FS is expressed by the following equation (11): ##EQU2## where Li is the space between the ferrite phases in measurement lines, and n is the number of times of measurements.
At present, there is no theoretical ground of how FS functions in response to an impact value.
Hence, two-phase stainless steels having various degrees of embrittlement are prepared and determined for Experimental C.sub.V (experimental value of absorption energy), H.sub.V F, H.sub.V A, FN and FS, to formulate an optimum estimation equation.
The optimum estimation equation refers to an equation where I.sub.error expressed by the following equation (5) reaches minimum: ##EQU3## where Estimated C.sub.V is estimated absorption energy; Experimental C.sub.V is experimental absorption energy; and i means each test material.
The estimation equation thus obtained is as shown in the following equation (12) where Charpy impact absorption energy can be expressed in terms of 4 examinable values, H.sub.V F, H.sub.V A, FN and SN:
Estimated C.sub.V =g.times.(1+eF.times.FS+hF.times.FS.sup.2) {(1-dF.times.FN/100-cF) (bA.times.H.sub.V A+aA)+(dF.times.FN/100+cF) (bF.times.H.sub.V F+aF)} . . . (12)
where g is a coefficient of correction; and eF, hF, dF, cF, bA, aA, dF, bF, and aF are constants.
If the respective constants are determined in estimation equation (12), the Charpy impact absorption energy of an actual machine can be obtained from non-destructively examinable and obtainable measurements from the actual machine, i.e. hardness of ferrite phase, H.sub.V F, hardness of austenite phase H.sub.V A, area ratio of ferrite phase, FN, and space between ferrite phases FS. A decrease in absorption energy indicates embrittlement and can thus serves as an indicator of degree of embrittlement.
According to the second aspect of the present invention, there can be provided a method of detecting the embrittlement of two-phase stainless steel in which Charpy impact absorption energy can be directly obtained from measurements capable of non-destructive examination, or estimated by examination, based on the mechanism of embrittlement of two-phase stainless steel as well as on the theory of Charpy impact absorption energy of two-phase material.
However, estimate accuracy worsened with a correlation coefficient of 0.876 as shown in FIG. 7, when Charpy impact absorption energy at room temperature is estimated non-destructively by the above formula (12) from hardness of ferrite phase, hardness of austenite phase, area ratio of ferrite phase, and space between ferrite phases using steel materials heated for 10,000 hours as input data besides the above-mentioned data, on the basis of the mechanism of embrittlement of two-phase stainless steel and the theory of Charpy impact absorption energy of two-phase material.
This worsening is probably due to the fact that a part of the steel materials heated for a long time at high temperature initiated to undergo significant grain boundary release on its fracture after impact testing. This grain boundary release is the phenomenon in which .alpha.- and .gamma.-phases are separated from each other along a brittle grain boundary having much precipitated carbide upon application of outer strength (arrows) on the interface therebetween (see FIG. 8). Because said grain boundary release results from the precipitation of carbide, the measurement of occupying ratio of carbide in grain boundary length is added as one parameter to permit further accurate estimation of Charpy impact absorption energy at room temperature to solve said problem.
The third aspect of the present invention is made under these circumstances and the object is to provide a method of detecting the embrittlement of two-phase stainless steel, wherein Charpy impact absorption energy at room temperature can be estimated with higher accuracy from the hardness of the ferrite phase, the hardness of the austenite phase, the area ratio of the ferrite phase, the space between the ferrite phases, and the occupying ratio of carbide in grain boundary length, in two-phase stainless steel.
In the third aspect of the present invention, the area ratio of the ferrite phase is determined in the following manner. Assuming that the ferrite phase (.alpha.-phase) is interspersed as shown in FIG. 9, the area ratio of the .alpha.-phase, FN (%), is as follows:
FN=l(sum of ferrite phase areas/total area) .times.100 . . . (13)
In the third aspect of the present invention, the space between the ferrite phases is determined by the equation (14). That is, in FIG. 10, the distance between ferrite island-shaped phases adjacent to each other is measured in 4 lines parallel to the Y axis and 3 lines parallel to the X axis to determine FS in the following equation (14): ##EQU4## where the distance between ferrite phases is FS, the distance between a ferrite phase and another ferrite phase is Li, and the affix i is the number of times of measurements.
In the third aspect of the present invention, the above occupying ratio of carbide in grain boundary length is determined in the following manner. Assuming that carbide (arrows) is interspersed as shown in FIG. 11, the occupying ratio (%) of carbide in grain boundary length is determined by the following equation (15). In FIG. 11, grain boundary is indicated as the line of grain boundary.
LC=(L.sub.C /L.sub.A).times.100 . . . (15)
where LC is the occupying ratio (%) of carbide in grain boundary length; L.sub.C is total length of carbide; and L.sub.A is the sum of grain boundary length.
Hereinafter, the third aspect of the present invention is described in detail.
Estimate accuracy worsened with a correlation coefficient of 0.876 when Charpy impact absorption energy at room temperature was estimated in a non-destructive manner by the previous estimation equation (the above equation (12) using steel materials heated at a high temperature for a long time (10,000 hours) in addition to a conventional data base (up to 3000 hours).
Hence, a fracture (i.e. a face appearing on destruction by testing) of the steel heated for a long time was examined, and it was found that the grain boundary, where ferrite phase/austenite phases were separated from each other, tended to show more fracture than conventional one. Further examination of this boundary under a transmission-type electron microscope indicated that precipitated carbide is larger than in conventional one.
We estimated that the Charpy impact absorption energy at room temperature of two-phase stainless steel is expressed by the following equation (16):
C.sub.V =g.times.{C.sub.V F.times.AF/100+C.sub.V A .times.AA/100+C.sub.V R.times.AS/100} . . . (16)
where AF and AA are the area ratios of ferrite and austenite phases respectively on a fracture of a test specimen after testing; AS is the area ratio of the released grain boundary; AF+AA+AS=100%; C.sub.V F is the absorption energy of the ferrite phase; C.sub.V A is the absorption energy of the austenite phase; and C.sub.V R is the absorption energy of the released grain boundary. The area ratio of released grain boundary AS (%) is a value obtained by dividing the sum of grain boundary areas on a fracture by the total area and it is determined by the following equation (17):
AS=(sum of grain boundary areas on fracture)/(total area).times.100. . . (17)
Now, the non-destructive handling with AS and C.sub.V R is described.
C.sub.V =AFC.sub.V F+AAC.sub.V A appearing on the equation (16) corresponds to a fundamental equation of the equation (12), and ASC.sub.V R adopted newly in the estimation equation is described as follows:
The relationship among the fracture ratio of released grain boundary AS observed on a fracture after testing, the occupying ratio of carbide in grain boundary measured by observation of the microstructure (the same meaning as "occupying ratio of carbide in grain boundary length" in the claims), and LC, is shown by plots in FIG. 12. In FIG. 12, the relationship between LC and AS is expressed as a straight line passing the common origin of materials A3, A4, and B2, but this relationship was previously formulated such that the straight line passes the origin, and usually k0 ranges from the+side to the-side. In addition, there is a material dependence between LC and AS, but there is a good correspondence between AS and LC. With respect to the material dependence, it was found that the area ratio of ferrite phase FN shows a good correspondence to the slope .beta. of the straight line expressing the relationship of AS-LS. The relationship between AS and LC is shown in the following equation:
AS=k0+.beta.LC . . . (18)
The relationship between the slope .beta. of the straight line and the area ratio of ferrite FN is shown in the following equation:
.beta.=C0+C1.times.FN . . . (19)
Hence, the area ratio of released grain boundary, AS, can be expressed by combination of the above equations (18) and (19), as follows:
AS={k0+(C0+C1.times.FN).times.LC} . . . (20)
The non-destructive estimation of the absorption energy of released grain boundary interface, C.sub.V R, is not feasible and is shown as a material constant because none is correlated with C.sub.V R as a state of grain boundary, although other absorption energies such as C.sub.V F (the absorption energy of the ferrite phase) and C.sub.V A (the absorption energy of the austenite phase) can be correlated with H.sub.V F (the hardness of the ferrite phase) and H.sub.V A (the hardness of the austenite phase) as shown in the relationships C.sub.V F=aF+bF.times.H.sub.V F and C.sub.V A=aA+bA.times.H.sub.V A respectively.
If the foregoing can hold, Charpy impact absorption energy can be estimated from H.sub.V F, H.sub.V A, FN, FS, and LC by use of the above formula (16). In the following equation (21), Charpy impact absorption energy is expressed in terms of 5 examinable values, H.sub.V F, H.sub.V A, FN, FS, and, LC:
Estimated C.sub.V =g.times.(1+eF.times.FS+hF.times.FS.sup.2) {(1-dF.times.FN/100-ef) (bA.times.H.sub.V A+aA)+(dF.times.FN/100+cF) (bF.times.H.sub.V F+aF)}+{( C0+C1.times.FN).times.LC+k0}/100.times.C.sub.V R . . . (21)
where g is a coefficient of correction; eF, hF, dF, eF, bA, aA, bF, aF, C0, C1, and k0 are constants; and C.sub.V R is a material constant.
The estimation equation (the above equation (21)) can be used for determination of Charpy impact absorption energy from measurements i.e. hardness of ferrite phase, H.sub.V F, hardness of austenite phase, H.sub.V A, area ratio of ferrite phase, FN, space between ferrite phases, FS, and occupying ratio of carbide, LC, all of which can be obtained by non-destructive examination of an actual machine. A decrease in absorption energy indicates embrittlement and can thus serves as an indicator of degree of embrittlement.
When C.sub.V was estimated from the above equation (21), the correlation coefficient was 0.896, indicating higher accuracy than in the equation (12).
According to the third aspect of the present invention, there can be provided a method of detecting the embrittlement of two-phase stainless steel capable of estimating Charpy impact absorption energy at room temperature with high accuracy from hardness of ferrite phase, hardness of austenite phase, area ratio of ferrite phase, space between ferrite phases, and occupying ratio of carbide in grain boundary length, of two-phase stainless steel.

BRIEF DESCRIPTION OF THE DRAWINGS
FIG. 1 is a characteristic drawing showing the effect of the estimation of impact absorption energy according to one example of the first aspect of the present invention.
FIG. 2 is a characteristic drawing showing the relationship between the area ratio of the fractured austenite phase and the area ratio of the ferrite phases.
FIG. 3 is a characteristic drawing showing the result of the estimation of impact absorption energy from the hardness of each phase and the fracture ratio of the austenite phase.
FIG. 4 is a characteristic drawing showing experimentally determined impact absorption energy at room temperature, the hardness of the ferrite phase and the fracture ratio of the austenite phase.
FIG. 5 is a characteristic drawing showing the relationship among experimentally determined impact absorption energy at room temperature, the hardness of the ferrite phase and the fracture ratio of the austenite phase.
FIG. 6 is a characteristic drawing showing the effect of the method of estimating impact absorption energy according to one example of the second aspect of the present invention
FIG. 7 is a characteristic drawing showing the effect of estimating impact absorption energy based on the equation (12).
FIG. 8 is a drawing for explaining grain boundary release.
FIG. 9 is a drawing for explaining the determination of the area ratio of the ferrite phase (.alpha.-phase).
FIG. 10 is a drawing for the determination of the space between the .alpha.-phases.
FIG. 11 is a drawing for explaining the occupying ratio of carbide in grain boundary length.
FIG. 12 is a characteristic drawing showing the relationship between the fracture ratio of released grain boundary (AS) and the occupying ratio of carbide (LC).
FIG. 13 is a characteristic drawing showing the effect of the method of estimating impact absorption energy according to one example of the third aspect of the present invention.
FIG. 14 is a characteristic drawing showing the relationship among experimentally determined impact absorption energy at room temperature, the hardness of the ferrite phase and the fracture ratio of the austenite phase.

DETAILED DESCRIPTION OF PREFERRED EMBODIMENTS
The first aspect of the present invention is described with reference to the following example.
Example 1
4 kinds of two-phase stainless steel (A to D) were prepared and heated at 350.degree. C., 400.degree. C., and 450.degree. C. for a long time (up to 3000 hours). The area ratio of the ferrite phase (not changed by heating) was 12% in material A, 30% in material B, 18% in material C, and 6.2% in material D. The hardness of the austenite phase scarcely changed, and Vickers hardness determined with 25 g loading before heating was 206 for material A, 212 for material B, 247 for material C, and 252 for material D.
Table 1 shows Charpy absorption energy Experimental C.sub.V at room temperature, Vickers hardness of the ferrite phase (1 g loading), H.sub.V F, and the area ratio AA (%) of the austenite phase obtained from fracture, of heated materials A to D (partially containing materials before heating).
TABLE 1______________________________________ Heating Heating Hour Experimental AAMaterials Temp. (.degree.C.) (h) C.sub.v (J) H.sub.v F (%)______________________________________A 350 1000 201 381 88 3000 159 439 85 400 300 192 409 100 1000 136 436 88 3000 105 540 84 450 300 227 409 100 1000 161 468 98 3000 94 566 84B 350 300 82 379 40 1000 73 402 76 3000 92 434 25 400 300 73 412 39 1000 37 437 54 3000 21 573 37 450 1000 55 465 46 3000 15 564 19C -- 0 135 303 42 350 300 114 314 46 1000 82 354 16 3000 73 448 40 400 300 97 404 49 1000 67 429 61 3000 60 472 19 450 300 116 376 73 1000 75 399 16 3000 59 527 7D -- 0 118 308 100 350 300 116 328 100 1000 114 353 100 3000 116 369 100 400 300 116 359 100 1000 94 383 100 3000 105 479 100 450 300 122 331 100 1000 117 370 100 3000 103 439 100______________________________________
FIG. 4 shows the relationship between Experimental C.sub.V and H.sub.V F. FIG. 4 shows that Charpy absorption energy of each material tends to decrease with increasing hardness of the ferrite phase. This indicates the propriety of proposed equations (2) and (3).
First, it was examined whether the equation (1) can hold or not. The equation was corrected as follows:
Estimated C.sub.V =g.times.{AA/100 (bA H.sub.V A+aA) +(1-AA/100) (bF H.sub.V F+aF)} . . . (22)
where g is a coefficient of correction.
The relationship between absorption energy (Estimated C.sub.V) which could be estimated from the results obtained using experimental data and the experimental results (Estimated C.sub.V) is shown in FIG. 3. Although there is a scattering of .+-.70 J therebetween, there is the 1:1 relationship. The scattering of .+-.70 J is considered practically small enough to estimate absorption energy, indicating that the equation (1) is appropriate.
As a result of examination of the method of estimating the fracture ratio of austenite (AA), it was found that as shown in FIG. 2, there is a correlation between AA and area ratio of ferrite phase (FN) with a correlation coefficient of 0.721 in the primary equation. The relationship was able to be expressed in the following equation (23):
AA/100=-2.628 FN/100+1.07 . . . (23)
Then, the equation (23) is combined with the equation (22) to obtain the optimum estimation equation (6) by which absorption energy (Estimated C.sub.V) was estimated. The relationship between absorption energy (Estimated C.sub.V) and experimental value (Experimental C.sub.V) is shown in FIG. 1 to provide estimation with approximately the same accuracy as in FIG. 3. The respective constants in equation (6) are: g=0.21, bA=-6.5, aA=2200 J, bF=-4.2, aF=1900 J, dF=-2.628, and cF=1.07. In FIG. 1, AA=-2.628.times. FN+106.67 (%).
Hence, the absorption energy at room temperature of an actual machine can be estimated from the equation (6) using hardness and area ratio determined for the ferrite phase and hardness determined for austenite phase of the actual machine.
According to the above example, the mechanism of embrittlement of two-phase stainless steel results from the decomposition of the ferrite phase into Cr-rich phase and Fe-rich phase by spinodal decomposition etc., and the ferrite phase of two-phase stainless steel is hardened with proceeding embrittlement. Because the austenite phase does not change at the temperature at which two-phase stainless steel is usually used, it is generally considered that its absorption energy becomes smaller as it becomes hardened. We, could arrive at the equation for estimating Charpy impact absorption energy by using measurements (hardness of ferrite phase, hardness of austenite phase, and area ratio of ferrite phase) examinable on an actual machine, from the foregoing idea and the simple assumption that the impact absorption energy of a material with two different phases is the sum of values obtained by multiplying the impact absorption energy of each single phase by its corresponding fracture area. This permits the non-destructive examination of the degree of embrittlement of an actual machine.
Then, the second aspect of the present invention is described with reference to the following example.
Example 2
4 kinds of two-phase stainless steel (A1, A2, B1, and C1) were prepared and heated at 350.degree. C., 400.degree. C., and 450.degree. C. for a long time (up to 3000 hours). The area ratio of the ferrite phase (not changed by heating) was 12% in material A1, 30% in material A2, 18% in material B1, and 6.2% in material C1. The hardness of the austenite phase scarcely changed, and Vickers hardness determined with 25 g loading before heating was 163 for material A1, 184 for material A2, 179 for material B1, and 190 for material C1.
Tables 2 to 5 show the hardness of the ferrite phase (1. g loading), H.sub.V F, the hardness of the austenite phase (25 g loading), H.sub.V A, and Charpy absorption energy, Experimental C.sub.V, the area ratio of the ferrite phase, FN, and the space between the ferrite phases, FS, obtained from the microstructure, of the respective heated materials A1, A2, B1, and C1 (partially containing materials before heating).
TABLE 2__________________________________________________________________________(Material A1)Nominal Image analysisferrite Heating Heating Fracture ratio (%) Ferrite area Ferriteamount temp. hours H.sub.v F H.sub.v A Ductility Cleavage Interphase ratio spaces(FN) (.degree.C.) (hr) H.sub.v (0.001) H.sub.v (0.025) C.sub.v (J) (D) (B) separation FN (%) FS (.mu.m)__________________________________________________________________________ No heating 0 307 163 269 100 0 0 10.3 78.912 350 300 363 157 209 100 0 0 11.4 62.0 1000 381 170 201 88 11 1 11.6 84.6 3000 439 162 159 85 13 2 9.7 78.9 10000 -- -- 88 26 64 10 -- -- 400 300 409 156 192 100 0 0 11.4 70.5 1000 436 165 136 88 10 2 9.2 83.6 3000 540 161 105 84 14 2 11.2 56.2 10000 -- -- 82 39 61 0.2 -- -- 450 10 409 152 227 100 0 0 12.1 71.1 100 468 159 161 98 2 0 12.3 73.1 3000 566 169 94 84 11 5 10.6 59.3 10000 -- -- 72 57 34 8 -- --__________________________________________________________________________ C.sub.v (J): Experimental C.sub.v (absorption energy at room temperature) Interphase separation: interphase separation (S), separated areas present in the boundary between and phases.
TABLE 3__________________________________________________________________________(Material A2) Image analysisNominal Heating Heating Fracture ratio (%) Ferrite area Ferriteferrite temp. hours H.sub.v F H.sub.v A Ductility Cleavage Interphase ratio spacesamount (FN) (.degree.C.) (hr) H.sub.v (0.001) H.sub.v (0.025) C.sub.v (J) (D) (B) separation FN (%) FS (.mu.m)__________________________________________________________________________ No heating 0 319 184 300 100 0 0 25.l 44.430 350 300 379 186 82 40 60 0 25.2 45.0 1000 402 181 73 76 23 1 20.9 43.6 3000 434 180 92 25 72 3 26.8 44.5 10000 -- -- 23 39 53 8 -- -- 400 300 412 182 73 39 59 2 24.8 50.7 1000 437 182 37 54 46 0 25.3 30.0 3000 573 182 21 37 59 4 18.9 46.4 10000 -- -- 15 34 50 16 -- -- 450 10 375 182 262 100 0 0 29.3 44.1 100 465 179 55 46 51 3 27.5 45.4 3000 564 182 15 19 73 8 15.9 46.8 10000 -- -- 13 3 71 26 -- --__________________________________________________________________________ C.sub.v (J): Experimental C.sub.v (absorption energy at room temperature) Interphase separation: interphase separation (S), separated areas present in the boundary between and phases.
TABLE 4__________________________________________________________________________(Material B1) Image analysisNominal Heating Heating Fracture ratio (%) Ferrite area Ferriteferrite temp. hours H.sub.v F H.sub.v A Ductility Cleavage Interphase ratio spacesamount (FN) (.degree.C.) (hr) H.sub.v (0.001) H.sub.v (0.025) C.sub.v (J) (D) (B) separation FN (%) FS (.mu.m)__________________________________________________________________________ No heating 0 303 179 135 42 42 6 16.8 53.018 350 300 314 190 114 46 48 2 19.7 38.4 1000 354 163 82 16 70 8 21.1 59.2 3000 448 181 73 40 51 4 18.0 58.8 400 300 404 167 97 49 44 3 18.9 51.8 1000 429 174 67 61 35 1 17.3 63.0 3000 472 174 60 19 58 8 16.7 53.9 450 10 376 171 116 73 24 1 16.6 84.8 100 399 178 75 16 83 1 13.9 66.8 3000 527 173 59 7 91 2 18.2 64.5__________________________________________________________________________ C.sub.v (J): Experimental C.sub.v (absorption energy at room temperature) Interphase separation: interphase separation (S), separated areas present in the boundary between and phases.
TABLE 5__________________________________________________________________________(Material C1) Image analysisNominal Heating Heating Fracture ratio (%) Ferrite area Ferriteferrite temp. hours H.sub.v F H.sub.v A Ductility Cleavage Interphase ratio spacesamount (FN) (.degree.C.) (hr) H.sub.v (0.001) H.sub.v (0.025) C.sub.v (J) (D) (B) separation FN (%) FS (.mu.m)__________________________________________________________________________ No heating 0 308 190 118 100 0 0 9.6 40.46.2 350 300 328 186 116 100 0 0 7.5 35.5 1000 353 203 114 100 0 0 8.8 52.6 3000 369 172 116 100 0 0 11.7 32.4 400 300 359 187 116 100 0 0 7.7 51.5 1000 383 206 94 100 0 0 6.3 54.5 3000 479 200 105 100 0 0 8.8 39.6 450 10 331 169 122 100 0 0 7.9 49.1 100 370 176 117 100 0 0 3.9 61.0 3000 439 195 103 100 0 0 9.0 37.8__________________________________________________________________________ C.sub.v (J): Experimental C.sub.v (absorption energy at room temperature) Interphase separation: interphase separation (S), separated areas present in the boundary between and phases.
FIG. 5 shows the relationship between Experimental C.sub.V and H.sub.V F. As can be seen from FIG. 5, the Charpy absorption energy of each material tends to decrease with increasing hardness of the ferrite phase. This indicates the propriety of proposed equations (8) and (9).
Then, the relationship between absorption energy (Estimated C.sub.V) which could be estimated by equation (12) from the experimental data and the experimental results (Estimated C.sub.V) is shown in FIG. 6. Although there is a scattering of .+-.20 J therebetween, there is the 1:1 relationship. The scattering of .+-.70 J according to the 1st aspect of this invention could be improved to the scattering of .+-.20 J by addition of a factor of space between ferrite phases.
The scattering of .+-.20 J is considered practically small to estimate absorption energy. Hence, the absorption energy at room temperature of an actual machine can be estimated by equation (12) on the basis of measurements of the hardness of the ferrite phase, the hardness of the austenite phase, the area ratio of the ferrite phase, and the space between the ferrite phases, of the actual machine.
According to the above example, the mechanism of embrittlement of two-phase stainless steel results from the decomposition of the ferrite phase into Cr-rich phase and Fe-rich phase by spinodal decomposition etc., and the ferrite phase of two-phase stainless steel is hardened with proceeding embrittlement. Because the austenite phase does not change at the temperature at which two-phase stainless steel is usually used, it is generally considered that its absorption energy becomes smaller as it becomes hardened. We could arrive at the equation for estimating Charpy impact absorption energy by using measurements (hardness of ferrite phase, hardness of austenite phase, area ratio of ferrite phase, and space between ferrite phases) examinable on an actual machine, from the foregoing idea and the simple assumption that the impact absorption energy of a material with two different phases is the sum of values obtained by multiplying the impact absorption energy of each single phase by its corresponding area ratio. This permits the non-destructive examination of the degree of embrittlement of an actual machine.
The third aspect of the present invention is described with reference to the following example.
Example 3
4 kinds of two-phase stainless steel (A3, A4, B2, and C2) shown below in Tables 6 to 9 were prepared and heated at;
350.degree. C., 400.degree. C., and 450.degree. C. for a long time (up to 10,000 hours). In addition to the 4 kinds of materials, Tables 6 to 9 show ferrite amount % (FN), heating temperature (.degree.C.), heating time (hr), ferrite strength (H.sub.v F, Hv (0.001)), austenite hardness (H.sub.v A, Hv (0.025)), room temperature absorption energy (Experimental C.sub.V) (J), fracture ratio % (ductility, AA; brittleness, AF; release grain boundary, AS), image analysis (ferrite area ratio FN (%)), ferrite space FS % (.mu.), and carbide occupying ratio LC (%)).
The ferrite amount (not changed by heating) was 10% in material A3, 25% in material A4, 18% in material B2, and 6.6% in material C2. The "ferrite amount" has a wider meaning and is considered to be scattered because the area ratio of the ferrite phase was image-processed with about 100.times. magnification photograph (5 to 6 areas). The hardness of the austenite phase scarcely changed, and Vickers hardness determined with 25 g loading before heating was 163 for material A3, 184 for material A4, 179 for material B2, and 190 for material C2.
Tables 6 to 9 show the hardness of the ferrite phase (1 g loading), H.sub.V F, the hardness of the austenite phase (25 g loading), H.sub.V A, and Charpy absorption energy, Experimental C.sub.V, the area ratio of the ferrite phase, FN, the space between the ferrites phases, FS, and the occupying ratio of carbide, LC, obtained from the microstructure. The test specimens were of the heated materials A3, A4, B2, and C2 (partially containing materials before heating).
TABLE 6__________________________________________________________________________ Ferrite Austenite Room temp. Fracture ratio (%) Image analysis Nominal phase phase absorption Release Ferrite Ferrite ferrite Heating hardness hardness energy grain area spaces Carbide amount % temp. Heating H.sub.v F H.sub.v A Experimental Ductility Brittle- boundary ratio FS occupyingMaterial (FN) (.degree.C.) hour (hr) H.sub.v (0.001) H.sub.v (0.025) C.sub.v (J) (AA) ness (AF) (AS) FN (%) (.mu.m) ratio LC__________________________________________________________________________ (%)A3 10 No 0 307 163 269 100 0 0 10.3 78.9 2 heating 350 1000 381 170 201 88 11 1 11.6 84.6 19 3000 439 162 159 85 13 2 9.7 78.9 37 10000 385 152 88 52 34 15 11.6 66.5 48 400 1000 436 165 136 88 10 2 9.2 83.6 35 3000 540 161 105 84 14 2 11.2 56.2 20 10000 439 176 82 39 61 0.2 13.5 61.9 44 450 1000 468 159 161 98 2 0 12.3 73.1 26 3000 566 169 94 84 11 5 10.6 59.3 29 10000 459 159 72 37 60 3 11.4 68.2 23__________________________________________________________________________
TABLE 7__________________________________________________________________________ Ferrite Austenite Room temp. Fracture ratio (%) Image analysis Nominal phase phase absorption Release Ferrite Ferrite ferrite Heating hardness hardness energy grain area spaces Carbide amount % temp. Heating H.sub.v F H.sub.v A Experimental Ductility Brittle- boundary ratio FS occupyingMaterial (FN) (.degree.C.) hour (hr) H.sub.v (0.001) H.sub.v (0.025) C.sub.v (J) (AA) ness (AF) (AS) FN (%) (.mu.m) ratio LC__________________________________________________________________________ (%)A4 25 No 0 319 184 300 100 0 0 25.1 44.4 2 heating 350 300 379 186 82 40 60 0 25.2 45.0 2 1000 402 181 73 76 23 1 20.9 43.6 1 3000 434 180 92 25 72 3 26.8 44.5 1 10000 390 217 23 9 90 1 26.6 38.6 1 400 300 412 182 73 39 59 2 24.6 50.7 3 1000 437 182 37 54 46 0 25.3 30.0 1 3000 573 182 21 37 59 4 18.9 46.4 1 10000 476 213 15 7 91 2 23.0 54.5 5 450 100 465 179 55 46 51 3 27.5 45.4 7 3000 564 182 15 19 73 8 15.9 46.8 12 10000 505 177 13 3 84 13 22.9 49.4 5__________________________________________________________________________
TABLE 8__________________________________________________________________________ Ferrite Austenite Room temp. Fracture ratio (%) Image analysis Nominal phase phase absorption Release Ferrite Ferrite ferrite Heating hardness hardness energy grain area spaces Carbide amount % temp. Heating H.sub.v F H.sub.v A Experimental Ductility Brittle- boundary ratio FS occupyingMaterial (FN) (.degree.C.) hour (hr) H.sub.v (0.001) H.sub.v (0.025) C.sub.v (J) (AA) ness (AF) (AS) FN (%) (.mu.m) ratio LC__________________________________________________________________________ (%)B2 18 No 0 303 179 135 42 42 6 16.8 53.0 15 heating 350 300 314 190 114 46 48 2 19.7 38.4 4 1000 354 163 82 16 70 8 21.1 59.2 14 3000 448 181 73 40 51 4 18.0 58.8 9 10000 351 166 55 5 94 1 18.3 62.7 4 400 300 404 167 97 49 44 3 18.9 51.8 16 1000 429 174 67 61 35 1 17.3 63.0 18 3000 472 174 60 19 68 8 16.7 53.9 10 10000 420 180 38 18 78 4 16.9 74.6 20 450 10 376 171 116 73 24 1 16.6 84.8 24 100 399 178 75 16 83 1 13.9 66.8 23 3000 527 173 59 7 91 2 18.2 64.5 20 10000 440 176 37 10 88 2 16.2 75.6 23__________________________________________________________________________
TABLE 9__________________________________________________________________________ Ferrite Austenite Room temp. Fracture ratio (%) Image analysis Nominal phase phase absorption Release Ferrite Ferrite ferrite Heating hardness hardness energy grain area spaces Carbide amount % temp. Heating H.sub.v F H.sub.v A Experimental Ductility Brittle- boundary ratio FS occupyingMaterial (FN) (.degree.C.) hour (hr) H.sub.v (0.001) H.sub.v (0.025) C.sub.v (J) (AA) ness (AF) (AS) FN (%) (.mu.m) ratio LC__________________________________________________________________________ (%)C2 6.6 No 0 308 190 118 100 0 0 9.6 40.4 0 heating 350 300 328 186 116 100 0 0 7.5 35.5 0 1000 353 203 114 100 0 0 6.8 52.6 0 3000 369 172 116 100 0 0 11.7 32.4 0 10000 377 216 96 78 21 1 6.4 15.2 0 400 300 359 187 116 100 0 0 7.7 51.5 0 1000 383 206 94 100 0 0 6.3 54.5 0 3000 479 200 105 100 0 0 8.8 39.6 0 10000 424 215 100 88 11 1 7.3 15.1 0 450 10 331 169 122 100 0 0 7.9 49.1 0 100 370 176 117 100 0 0 3.9 61.0 0 3000 439 195 103 100 0 0 9.0 37.8 0 10000 448 201 96 39 58 3 6.0 18.1 0__________________________________________________________________________
A correlation coefficient of 0.884 as shown in FIG. 13 is obtained by plotting the relationship between the Charpy absorption energy (Experimental C.sub.V) and the estimated absorption energy (Estimated C.sub.V) from the above equation (21) using the above values. The coefficient of correction and the constants in equation (21) were calculated using a method known to the art.
The effect according to the above example is as follows:
The correlation of room temperature Charpy impact absorption energy C.sub.V (0.876) from the estimation equation (12), i.e. Estimated C.sub.V =g.times.(1+ef.times.FS+hF.times.PS.sup.2) {(1-dF.times.FN/100-ef) (bA.times.H.sub.V A+aA)+(df.times.FN/100+ef) (bF .times.H.sub.V F+aF)}, worsened using data on the materials heated for a long time (10,000 hours) in addition to the previous data base (up to 3000 hours). Hence, we examined the above estimation equation (16) i.e. C.sub.V =g.times.{AF/100.times.C.sub.V F+AA/100.times.C.sub.V A+AS/100.times.C.sub.V R}.
AS can be expressed in terms of FN and LC in the above formula (20), i.e. AS={k0+ (C0+C1.times.FN).times.LC}, so that the above formula (21), i.e. Estimated C.sub.V =g.times.(1+eF.times.FS+hf.times.FS.sup.2) {(1-dF.times.FN/100-eF) (bA.times.H.sub.V A+aA)+(dF.times.FN/100+eF) (bF.times.H.sub.V F+aF)}+{k0+(C0+C1.times.FN).times.LC}.times.C.sub.V R was obtained to give a good correlation of 0.884 than in the previous estimation equation (12).
The relationship between the absorption energy (Estimated C.sub.V) which could be estimated from the experimental data and the experimental results (Experimental C.sub.V) is shown in Table 13. Although there is a scattering of .+-.22.5 J therebetween, there is the 1:1 relationship. As compared with the scattering of .+-.27.5 J as shown in FIG. 7 according to the previous equation (12), the scattering of .+-.22.5 J is practically small to estimate absorption energy. Hence, the absorption energy at room temperature of an actual machine can be estimated by equation (21) on the basis of measurements of the hardness of the ferrite phase, the hardness of the austenite phase, the area ratio of the ferrite phase, the spaces between the ferrite phases, and the occupying ratio of carbide, of the actual machine.
FIG. 14 shows the relationship between Experimental C.sub.V and H.sub.V F. As can be seen from FIG. 14, the Charpy absorption energy of each material tends to decrease with increasing hardness of the ferrite phase. FIG. 12 shows the relationship between the fracture ratio of released grain boundary (AS) and the occupying ratio of carbide (LC).

Number	Name	Date
4428781	Norstrom	Jan 1984
4461168	Kobayashi	Jul 1984
4719583	Takafuji et al.	Jan 1988

Number	Date	Country
04235347	Aug 1992	JPX
2 150 305	Jun 1985	GBX

Method of detecting the embrittlement of two-phase stainless steel

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