JP2013244492A - METHOD FOR MANUFACTURING ROUND CAST SLAB FOR MAKING HIGH Cr STEEL SEAMLESS STEEL PIPE - Google Patents

Abstract

PROBLEM TO BE SOLVED: To provide a method for continuously casting a round cast slab for making a high Cr seamless steel pipe, sufficiently restrained at a practical level from the occurrence of a crack at an axis part, particularly a shrinkage hole formed in the last stage of coagulation and an A-type crack caused by the shrinkage hole as well as a C-type crack, and having a small cast slab camber.SOLUTION: In continuously casting a round cast slab for making a high chromium steel seamless steel pipe, a strand containing uncoagulated molten steel inside is subjected to axis part coagulation former stage forced cooling with a water quantity density Qof 30-90 L/m/min over at least a section from a position at which the axis part solid phase ratio fs of the strand is 0.2 up to a position at which the fs is 0.5, and then is subjected to axis part coagulation former stage forced cooling with a water quantity density Qof 20-60 L/m/min smaller than the cooling water quantity density at the end of the axis part coagulation former stage forced cooling, over at least a section from a position at which the fs is 0.8 up to a position at which the axis part temperature of the strand is (Ts-145)°C.

Description

  The present invention relates to a round slab used for the production of martensitic high chromium seamless steel pipes used for oil well drilling, in particular, high Cr seamless steel pipes having a Cr content of 12 to 18% by mass. More particularly, the present invention relates to a method for producing a round slab used for producing a 13Cr seamless steel pipe (API-13Cr steel pipe). The 13Cr seamless steel pipe round slab particularly refers to a high chrome steel seamless steel pipe round slab having a Cr content of 12.7 to 13.3 mass%.

  Seamless steel pipes are generally prepared with a round billet (round slab) as a starting material, drilled by the Mannesmann drilling method, then stretched by a rolling machine such as an elongator, plug mill or mandrel mill, and further by a sizer or stretch reducer. Manufactured by a series of steps to make the diameter constant.

  As a method for preparing such a round billet, a method in which a round billet is directly continuously cast is known. In the case of low carbon steel, a round billet having a good inner quality in a cast state can be obtained. However, in the case of high Cr steel, especially 13Cr steel, 15Cr steel, and 17Cr steel, in the cast state, internal cracks due to porosity and segregation are likely to occur inside the round billet, and wrinkles occur during Mannesmann drilling. There is a problem that it is likely to occur. Therefore, for example, as disclosed in Patent Document 1, the porosity is obtained by subjecting the slab having a rectangular cross-section corresponding to three times or more to the cross-sectional area of the round billet by continuous rolling and carrying out a block rolling with large reduction. It has been performed to improve the internal quality by mechanically pressing.

  Although this method can obtain a round billet (round slab) having an excellent internal quality, there is a problem that the cost is high. In order to solve this problem, for example, Patent Documents 2 to 4 disclose a series of means for applying unsolidified reduction when manufacturing a round billet (round cast piece) by continuous casting. Therefore, it is possible to prevent the generation of internal cracks, center porosity, center segregation, and axial center cracks.

  However, all of the means described in Patent Documents 2 to 4 involve a process of applying mechanical reduction to an unsolidified portion in a continuous casting process of a round billet (round cast slab) and discharging unsolidified molten steel to the upstream side. This includes the essential problem that a decrease in product yield is inevitable. In addition, there is a problem in that the equipment for mechanical reduction becomes large and equipment costs increase.

On the other hand, Patent Document 5 proposes a secondary cooling method that uses thermal shrinkage during slab cooling as a method for reducing the center porosity and center segregation of continuously cast slabs. In continuous bloom or billet casting of steel, the final solidification is forced until the solid fraction at the center of the slab reaches 0.99 or more from the position 0.1 to 2.0 m before the casting direction of the residual molten metal pool. A method of cooling the slab surface with a water density of 100 to 300 liters / (min · m ² ) in the cooling zone is shown (Patent Document 5: refer to claim 1).

JP 61-140301 A Japanese Patent Laid-Open No. 10-249490 JP-A-11-216547 JP 2000-288704 A JP 2001-62550 A (Patent No. 3401785)

  With the means described in Patent Document 5, it is estimated that the problems included in the means described in Patent Documents 2 to 4, that is, problems such as a decrease in product yield and high equipment costs can be solved to some extent. However, the low carbon steel and 1% Cr steel cited as examples in Patent Document 5 have a relatively short solidification section (liquidus-solidus temperature interval) and are easily segregated during solidification. The content of is low. For this reason, it is difficult for the shaft center part crack which is a problem in the present invention to occur. On the other hand, 12-18% Cr steel used for drilling oil wells has a feature that the solidification section is long and Cr is easily segregated during solidification. Therefore, even if the means described in Patent Document 5 is applied as it is, in these high Cr steels, A-type and C-type axial center cracks described later frequently occur, and sufficient effects cannot be obtained. In addition, depending on the water density applied to the slab surface in the forced cooling zone at the end of solidification, excessive slab warpage may occur in the product round slab, which may hinder the stable operation of continuous casting. Among them, 13Cr steel has high strength by increasing the carbon concentration as compared with 15Cr steel and 17Cr steel. Therefore, the solidification zone is remarkably wide, and the A-type crack is likely to occur remarkably.

  The present invention solves the problems of the above-mentioned Patent Document 5, and the axial crack, particularly the shrinkage hole generated at the end of solidification described later and the occurrence of A-type crack caused by this, along with the C-type crack, is a practical level. It is an object of the present invention to provide a continuous casting method for round slabs for pipe making of high Cr seamless steel pipes, which can be sufficiently suppressed by slab and has small slab warpage.

  The present inventor has conducted a detailed investigation on the cause of defects that occur in the continuous casting process of high-Cr seamless steel pipe round slabs. As a result, in the process of continuous casting, solidification at the axial center of the strand starts. Immediately after that, water cooling is strengthened to strictly prevent the occurrence of so-called V segregation, which contributes to the suppression of the occurrence of the A-type crack, and further, it is assumed that the axial center portion of the strand does not contain macro segregation. Thus, the present invention has been completed by discovering that continuing cooling with a low amount of water can effectively reduce cracks due to shrinkage holes that occur in the subsequent cooling process even after complete solidification.

Specifically, the continuous casting method of the high-Cr seamless steel pipe pipe round cast piece according to the present invention continuously casts a high-Cr seamless steel pipe pipe round cast piece containing 12 to 18% of Cr by mass ratio. Hitting
For a strand having a circular cross section containing unsolidified molten steel inside in the process of continuous casting, the water density is at least over a section where the axial solid phase ratio fs of the strand is 0.5 from the position of 0.2. Between the position where the axial center solid phase ratio fs becomes 0.5 and the position where the axial center solid phase ratio fs becomes 0.5 after the forced cooling of the axial center solidification in which Q ₁ is 30 to 90 L / m ² / min. The water density Q ₂ is ₂₀ to 60 L / m ² / min over the interval from the position where the fs is 0.8 to the axial center temperature of the strand is (Ts-145) ° C. there are, and water amount density Q _2, characterized in that performing the axis portion coagulation year of forced cooling at the end of the cooling water density Q _1E smaller axial portion solidified later forced cooling.
Here, the axial solid part ratio fs means the mass ratio of [solid phase / (solid phase + liquid phase)] in the strand axial part, and Ts is the solid phase of the molten steel used for continuous casting. Refers to the line temperature.

  In the above invention, it is preferable that the forced cooling of the axial center solidification first phase is started from a position where the axial solid phase ratio fs is 0.01 to 0.2.

  In each of the above inventions, it is preferable that the cooling water density provided in the forced cooling of the axial center solidification is reduced toward the downstream side of the strand.

  In each of the above inventions, it is effective to apply the high chromium steel to 13Cr steel containing 12.7 to 13.2% Cr by mass. Moreover, it is desirable to take the diameter of the round cast slab for seamless steel pipe production between 170 and 330 mm.

  According to the present invention, a round slab for a high-Cr seamless steel pipe made of high-Cr seamless steel pipe having a practically low level of cracking in the axial center portion and a small slab warpage, by using only water-cooling means, regardless of conventionally proposed mechanical reduction. Can be continuously cast. In particular, according to the present invention, it is possible to highly prevent V segregation cracking that occurs during continuous casting of high-Cr seamless steel pipe round slabs. As a result, the occurrence of A-type cracking in the shaft center is reduced to a very high level. can do. As a result, the round slab obtained according to the present invention can be subjected to a normal diameter reduction rolling after reheating, and can be used as it is in a pipe making process, and the defect occurrence rate appearing in a product steel pipe can be made extremely low. it can.

It is a conceptual diagram which shows the cooling zone and arrangement | positioning in the continuous casting installation of the round slab for seamless steel pipe pipe making for implementing this invention. It is a typical explanatory view of an internal defect which appears in a round slab for pipe making of high Cr steel seamless steel pipe. (A) A type crack, (b) B type crack, (c) C type crack It is an explanatory view schematically showing a water density Q _1, Q ₂ to apply the solidified state fs and the axial center temperature (Ts-X) ℃ the axis of the strands as the horizontal axis in the present invention. It is explanatory drawing of A type crack and its crack length. It is explanatory drawing about the measuring method of the quantity of curvature of a round slab. It is a relationship figure (a figure) between the amount of applied water in the axial center solidification late forced cooling and the compression stress-tensile stress transition point in the axis part, and a relation figure (b figure) with the warp which appears in a product round cast piece. The application pattern of the solidification state-applied water amount density of the axial center solidification early forced cooling and axial center solidification late forced cooling which concern on this invention is shown.

  FIG. 1 is a conceptual diagram showing a cooling zone and its arrangement in a continuous casting facility for carrying out the present invention. As shown in FIG. 1, the molten steel injected into the molten steel from the tundish (not shown) into the continuous casting mold 1 having a circular cross section has a solidified shell grown while passing through the secondary cooling zone 2 equipped with a spray nozzle. A strand S having unsolidified molten steel is formed inside, and after complete solidification, the strand S is straightened by the straightening band 5, and then is made into a round cast piece of seamless steel pipe having a predetermined length by a cutting means (not shown). In the present invention, the continuous cooling process, particularly the secondary cooling zone 2, followed by the axial solidification early forced cooling zone 3 and the axial solidification late forced cooling zone 4 forcibly cools at an appropriate water density, It aims to reduce defects that occur inside the round cast slabs for making Cr steel seamless steel pipes. In addition, the axial center part solidification early forced cooling zone 3 and the axial center solidification late forced cooling zone 4 are a strand axial center part provided in the downstream area side of the secondary cooling zone 2 normally provided in the continuous casting equipment. Refers to a cooling zone for applying compressive stress.

  Hereinafter, the case where the present invention is applied to continuous casting of a round cast piece for 13Cr seamless steel pipe production will be described as an example. When 13Cr steel is continuously cast using a continuous casting facility, there are various internal defects in the round product slab depending on the continuous casting conditions such as the water density of the secondary cooling zone and the forced cooling zone of the axial center thereafter. A crack in the shaft center occurs. Typically, these axial cracks are classified into three types: (1) A type, (2) B type, and (3) C type crack. Here, as shown in FIG. 2 (a), the A-type axial center crack is a relatively small crack defect that occurs in the central portion of the cross section perpendicular to the casting direction of the strand. This is a star-shaped crack generated from the shrinkage hole generated in As shown in FIG. 2 (b), the B-type axial center crack is a V-shaped crack that occurs in the cross-section of the strand in the casting direction, and is derived from a V-shaped segregation that occurs from the middle to the end of solidification. As shown in FIG. 2 (c), the C-type axial center crack is a crack having a relatively large opening that appears in a cross section perpendicular to the casting direction of the strand. This is caused by expansion of the shrinkage hole due to the tensile stress at the time of recuperation applied to the part.

In the present invention, when casting a round slab using a continuous casting machine, after the secondary cooling, the forced cooling of the axial center solidification early stage is performed, and then the forced cooling of the axial center solidification late stage is performed. FIG. 3 shows the water amount density Q1 in the forced cooling of the _first axial solidification applied in the present invention and the water density Q2 in the forced cooling of the _second axially solidified phase in the solidification state (fs and axial center of the strand central portion). It is explanatory drawing typically shown with respect to temperature (Ts-X) (degreeC), and shows the example of the relationship with the water amount density with respect to the typical solidification state actually applied with the continuous line. The area indicated by (A) in the figure indicates the range of the axial center solidification state (solid phase ratio fs) -water density that can be applied in the forced cooling of the axial center solidification early stage, and the area indicated by (B) in the figure indicates the axial center part. The solidified state of the axial center (solid phase ratio fs or axial temperature (Ts-X)) applicable to the forced cooling in the latter phase of solidification indicates the range of the water density, and the solid line indicates the actual applied solidification-water density. The relationship curve is shown.

In this example, the applied water volume density is from the water volume density Q _{0 at the} end of the secondary cooling zone to the water volume density Q ₁ for forced cooling of the shaft center solidification first period at the shaft center solid fraction fs: 0.2: 70 L / After switching to m ² / min and continuing until the solid phase ratio fs reaches 0.7, the water density Q ₂ for forced cooling in the late stage of solidification of the axial center is switched to 40 L / m ² / min. Then, at a temperature at which the shaft center temperature is lowered by 30 ° C. from (Ts-145) ° C., the water density Q ₃ is further switched to 10 L / m ² / min, and this state is the shaft center temperature: (Ts-255 ) Continues to ° C.

( Forced cooling conditions in the early stage of solidification of the shaft center and its technical significance )
As shown in the region (A) of FIG. 3, the forced cooling of the axial center solidification first phase is a water amount at least over a section where the axial center solid phase ratio fs of the strand is 0.5. density _{Q 1} is intended to provide cooling water of 30~90L ^/ m 2 ^/ min into a strand surface.

Table 2 shows the first stage of solidification of the axial center when a molten steel of 13Cr steel having the composition shown in Table 1 is continuously cast using a vertical bending type continuous casting equipment having a water-cooled copper mold having an inner diameter of 210 mm of the type shown in FIG. The relationship between the application time of forced cooling and the A type shaft center part crack length and B type shaft center part crack presence which appear in the round cast slab for 13Cr steel seamless steel pipe production is shown. In Table 2, the condition (a) is an axis in which the water density Q ₁ is in the range of 30 to 90 L / m ² / min over a section where the axial center solid fraction fs is 0.2 to 0.5. After forced cooling in the first stage of solidification of the core, the state is continued until the axial solid fraction fs becomes 0.7, and then the water density is decreased so that the axial temperature of the strand becomes (Ts-145) ° C. This corresponds to the case where the axial center solidification late forced cooling is performed over the interval until the axial center solidification, and this is the case where the axial center solidification early forced cooling is properly performed. On the other hand, the conditions (b) and (c) are the periods in which the axial solid phase ratio fs is 0.3 to 0.5 and 0.1 to 0.4, respectively. And then the water density is decreased and the axial center solidification late forced cooling is performed over the interval until the axial center temperature of the strand reaches (Ts-145) ° C., respectively. This corresponds to the case where the start of forced cooling in the early stage of solidification of the axial center is delayed, or is terminated early. On the other hand, the condition (d) is a case where no forced cooling is performed at all before the axial solidification after the secondary cooling. In addition, axial solidification late forced cooling was performed so that the range of the area | region (B) of FIG. 2 might be satisfy | filled in any case.

  The axial solid part ratio fs means the mass ratio of [solid phase / (solid phase + liquid phase)] in the strand axial part. For example, Izuo Ohnaka, “Introduction to Computer Heat Transfer and Solidification Analysis 1985”. It can be obtained by heat transfer solidification calculation such as “4.3.2 Solidification analysis of alloy” described on pages 196 to 208 of “Year Maruzen”. Ts refers to the solidus temperature of bulk molten steel subjected to continuous casting, and can be calculated using, for example, commercially available phase diagram calculation software “Thermocalc” (Thermocalc software Inc.).

  From Table 2, when the application time of forced cooling of the axial center solidification early phase is within the proper range, the length of the A type axial center crack appearing in the axial center is drastically reduced, but the start of forced cooling of the solidified early phase is delayed It can be seen that when it is finished early, it is difficult to sufficiently reduce the occurrence of A-type axial center cracks. Further, it can be seen that when the forced cooling is not performed in the early stage of the axial center solidification or when the start thereof is delayed, the B type axial center crack is generated. As described above, the reason why the A type axial center crack is reduced together with the B type axial center crack by optimizing the forced cooling in the first stage of solidification is the cause of the V-shaped segregation generated in the strands and the A type crack. It is presumed that this is because the shrinkage pores are drastically reduced. In other words, cracks in the center of the shaft are remarkably center segregated such as V-shaped segregation or zaku, which occurs during the solidification process, and the solidified from the shaft center to the surface after solidification in the portion that is in the unsolidified or vacant state even at the final solidification position Although it occurs when tensile stress is applied, it is presumed that it became possible to reduce the cause of these axial cracks by optimizing the pre-solidification forced cooling.

  By the way, the V-shaped segregation generated in the continuous casting process is a direct cause of the B-type crack, but in the V-shaped segregation generation period of the axial center solid fraction fs: 0.3 to 0.7. It is presumed that the so-called concentrated molten steel is caused by instantaneous and periodic inflow from the upstream side of the strand. Therefore, in order to suppress this inflow and suppress the occurrence of V-shaped segregation, it is necessary to enhance the cooling of the strands so that a sufficient compressive stress is applied to the shaft center portion during the V-shaped segregation generation period. it is conceivable that. However, the above experimental results are not sufficient, and the solid phase ratio fs of the axial center reaches 0.2 at the latest, particularly immediately after the start of coagulation in the axial center. From this stage, it is shown that it is necessary to perform forced cooling in the early stage of solidification of the shaft center.

As described above, it is necessary to perform the forced cooling of the axial center solidification first phase at least over a section where the solid phase ratio fs of the axial center portion of the strand is 0.5. However, that is not enough. The applied water density in that section needs to be in the range of 30 to 90 L / m ² / min. The applied water volume density is such that the volume of the shaft center portion corresponds to the solidification shrinkage of the liquid phase portion of about 4 to 5% in the volume ratio generated in the solidification process when the shaft center portion fs is 0.2 or more in continuous casting. It is the right thing to make a change. When the applied water density is less than 30 L / m ² / min, the occurrence of V-shaped segregation cannot be sufficiently suppressed. As a result, even if the axial center solidification late forced cooling described later is appropriately performed, the A type The occurrence of cracks in the shaft center cannot be sufficiently suppressed. On the other hand, when the applied water density exceeds 90 L / m ² / min, uniform cooling over the entire circumference of the strand becomes difficult, resulting in surface cracks (lateral cracks) and uncorrectable bends in the strands (round cast pieces). There is a fear.

( Conditions for forced cooling at the end of solidification and its significance )
As described above, the pre-solidification forced cooling has significance as a condition for suppressing the occurrence of defects that are the starting points of V-shaped segregation or A-type axial center cracks. On the other hand, the forced solidification late-solidification directly suppresses the occurrence of V-shaped segregation and also causes the occurrence of A-type axial center cracks (including A-type cracks during recuperation described later) that occur in the final solidification stage. It has a meaning to suppress.

In the present invention, the axially solidified late forced cooling is performed over a period from the position where the axial solid phase fraction fs is at least 0.8 to the axial temperature of the strand reaching (Ts-145) ° C. Te, water flow rate _{Q 2} is performed to provide 20~60L ^/ m 2 ^/ min. In this case, the water density must be set to be lower than the water density at the end of the forced cooling of the axial center solidification first period.

  In the present invention, as described above, the coagulation end-stage forced cooling is performed from the position where fs is 0.8 to the position where the temperature of the axial center is (Ts-145) ° C. This region corresponds to a region where an A type crack occurs. In the upstream region where fs is less than 0.8, the fluidity of the molten steel in the shaft center portion is high and A-type cracks do not occur, while the temperature of the shaft center portion falls below (Ts-145) ° C. For example, a hot strength that can withstand the tensile stress (estimated to be about 8 MPa) generated in the shaft center member is generated. In the above section, because of the film-like residual molten steel remaining in the shaft center portion, the hot strength of the shaft center portion is low, and even if a slight tensile stress is applied, it develops into an A-type crack.

Note that the hot strength of the shaft center part is obtained by performing a high-temperature hot tensile test at a low speed of 1 × 10 ⁻³ / s in the solidification process of 13Cr steel, which is a typical applicable steel type of the present invention. Can be measured. As a result of such measurement, it is determined that the temperature at which a significant cross-sectional reduction rate is obtained in the solidification process of 13Cr steel is 1300 ° C. The difference from Ts is 145 ° C., and based on this difference, it is determined that the application range of the above-mentioned axial center solidification late forced cooling becomes (Ts-145) ° C.

In the continuous solidification process of 13Cr steel, the temperature of the shaft center portion is (Ts-145) ° C. from the position where the solid phase ratio fs of the shaft center portion of the strand is 0.8 in the continuous casting process of 13Cr steel. It is necessary that the water density of the cooling water applied to the outer peripheral surface of the strand is 20 to 60 L / m ² / min. The water density is set to 20 L / m ² / min or more when the temperature density is less than 20 L / m ² / min, the temperature gradient between the strand surface and the shaft center is small, and a sufficient compressive stress is applied to the strand shaft center. This is because they cannot. On the other hand, when the water density is 60 L / m ² / min or less, if it exceeds 60 L / m ² / min, the tensile stress applied to the shaft center portion at the time of reheating after completion of cooling becomes too large, and the C-type crack is caused. This is because it occurs. Furthermore, this is because the risk of warping remaining in the round product slab obtained by cutting the strand becomes significant. The water density is obtained by dividing the amount of water per unit time (L / min) given to the cooling zone by the surface area of the strands in the cooling zone.

FIG. 6A is a diagram showing the relationship between the water amount density of the axially solidified late-stage forced cooling and the compressive stress-tensile stress transition point in the axial center. As is clear from FIG. 6 (a), by performing forced cooling at the end of solidification of the shaft center, the stress applied to the compression stress-tensile stress (the stress applied to the strand shaft in the continuous casting process is changed from the compression side to the tension side). The distance from the molten steel meniscus in the continuous casting mold to the downstream side) and the distance reaches a maximum value at a water density of 60 L / min / m ² . Further, from FIG. 6 (b), when the water amount density of the axial center solidification late forced cooling increases, the slab warpage appearing in the product round slab increases, and the water amount density exceeds 60 L / min / m ² . It can be seen that it increases significantly.

  By performing the above-mentioned forced cooling of the shaft center solidification at an appropriate water density, generation of A-type cracks can be remarkably suppressed and slab warpage can be reduced. However, after that, for example, when the strand is left in an air-cooled state, the outer peripheral portion of the strand is reheated, and tensile stress is again applied to the shaft center portion. As a result, an A type crack (A type at the time of recuperation) Cracks) may expand.

The expansion of the A-type crack at the time of recuperation is performed after the end of the forced cooling at the end of solidification of the axial center, and further, until the temperature of the axial center of the strand decreases, for example, 10-20 L / m ² / It can prevent by performing cooling by min.

  The A-type crack at the time of recuperation is caused by excessive tensile stress in the periphery of the shrinkage hole having a diameter of about several millimeters generated in the strand shaft center part in the continuous casting process or the shrinkage hole still remaining after the forced cooling of the shaft center part after the solidification. It is presumed to be caused by Therefore, in order to reduce this, it is necessary to suppress the reheating of the slab so that the tensile stress of the shaft center does not become excessive in the generated temperature section. More preferably it continues.

  It is preferable that the additional forced cooling section for preventing the A-type crack at the time of recuperation corresponds to the generated temperature section. Specifically, taking 13Cr steel as an example, the additional forced cooling is performed until the temperature of the strand axis decreases to (Ts-255) ° C. or lower following the forced cooling after the axial center solidification. Preferably it is done.

  As described above, the axial center solidification early forced cooling and the axial central solidification forced cooling are appropriately performed, so that the axial center cracking of high chrome steel round cast pieces represented by 13Cr steel is almost completely achieved at the practical level. It is possible to continuously cast a round slab for pipe making of high Cr seamless steel pipe with reduced slab warpage. Hereinafter, preferred conditions for forced cooling will be described.

In the axial solidification pre-stage forced cooling, the water density Q ₁ is at least over the interval where the axial solid phase ratio fs is 0.5 from the position where the axial solid phase ratio fs is 0.2 so as to satisfy the region (A) shown in FIG. Is necessary to give 30 to 90 L / m ² / min. As the conditions before the start, the secondary cooling conditions in the continuous casting of normal round pipes for seamless steel pipe production can be applied as they are. However, before reaching fs: 0.2, for example, forced cooling can be started from the position of fs: 0.01 by the water density corresponding to the forced cooling in the first stage of solidification of the shaft center portion. Can be further enhanced. If forced cooling of the axial center solidification first phase is started before fs: 0.2 is reached, there is also an effect that the surface temperature of the slab is lowered early to increase the cooling efficiency.

  The water density applied in the forced cooling of the axial center solidification first phase can be freely set as long as it does not deviate from the region (A) shown in FIG. For example, in the section, it is possible to gradually increase or decrease in accordance with the solidification state of the strand shaft center part or the formation state of the solidified shell.

The forced cooling of the axial center solidification first phase can be continued until fs: 0.8 is exceeded beyond the region (A) shown in FIG. During this period, the cooling water density needs to be maintained in the range of 30 to 90 L / m ² / min. Preferably, after exceeding fs: 0.5, the water amount density is gradually or stepwise reduced so as to reduce to the cooling water amount density of the subsequent forced cooling of the axial center solidification.

As shown in FIG. 3, the switching from the forced cooling of the axial center solidification early period to the forced cooling of the late axial center solidification is performed after reaching fs: 0.5 until reaching 0.8. The timing can be arbitrarily determined according to the solidification state of the strand shaft center portion or the formation state of the solidified shell. However, the cooling water density at the time of switching needs to be lower than the water density Q _1E at the end of the early cooling of the axial center solidification, and lower than the water density Q ₂ at the start of the forced cooling of the latter of the axial solidification. There is.

  Although the axially solidified late-stage forced cooling can be freely performed within the region shown in FIG. 3, it is preferable to reduce it gradually or stepwise. This makes it possible to more effectively prevent the round cast slab from being bent and the A-type crack during recuperation in the continuous casting process.

  The present invention can be applied to 15Cr steel and 17Cr steel in addition to 13Cr steel. The application conditions at that time are basically the same as in the case of 13Cr steel. However, since the solidification / segregation state of the shaft center portion changes depending on the Cr content, the addition of other alloy elements, etc., it is desirable to correct the conditions in consideration of this point.

  The present invention can be applied to continuous casting of seamless steel pipe round cast pieces having a diameter of 170 to 330 mm. In these cases, it is not basically necessary to change the conditions of the forced cooling before the solidification of the axial center and the forced cooling after the solidification of the axial center. However, since the solidification / segregation state of the shaft center portion is changed by changing the mold size or the continuous casting conditions accompanying it, it is desirable to correct the conditions in consideration of this point.

High Cr steel having the composition (mass%) shown in Table 3 was continuously cast using a cylindrical mold having an inner diameter of 210 mm. In the continuous casting, the conditions of the forced cooling at the early stage of solidification of the axial center and the forced cooling at the later stage of solidification of the axial center were taken in the patterns of (a) to (f) in FIG. For example, in pattern (a), after the initial cooling of the axial center solidification is performed at a water density of 70 L / m ² / min over a section from fs: 0.1 to fs 0.7, the axial solidification late forced Cooling was performed at a water density of 60 L / m ² / min from fs: 0.7 to axial temperature: (Ts-145) ° C., and further to axial temperature: (Ts-255) ° C. This is a case where the water density is 10 L / m ² / min. The other patterns (b) to (f) are also subjected to forced cooling following the process shown in the figure.

  The average length of A-type axial center cracks (including A-type cracks during recuperation) and C-type cracks of the obtained product round cast slab, and the degree of slab bending were evaluated. The evaluation results are also shown in Table 4. As shown in FIG. 5, the length of the A-type crack means the length (mm) of the crack extending from the shrinkage hole, and the evaluation is based on the A-type crack observed in the cross-sections of a number of round cast pieces. The average value of the lengths of the shafts was determined, and a case where the axial center crack length was 5 mm or less was regarded as acceptable. According to the knowledge of the present inventor, although there is a slight difference depending on the pipe making conditions, if the crack length of the billet shaft center part can be suppressed to 5 mm or less, the inner surface blurring defect of the product after pipe making is greatly reduced. This is because it has been empirically confirmed that this can be reduced. In Table 4, it can be confirmed that in the example of the present invention, the crack length can be suppressed to 5 mm or less, and no billet bending occurs. About the C type crack, it evaluated by the presence or absence of the C type crack shown in FIG.2 (c), and its passing length. The slab bending was evaluated based on the bending amount shown in FIG.

(Pipe making test)
It has the components and compositions shown in Table 3, and No. 1 and no. A pipe making test was performed on the round cast slab manufactured according to No. 5. Pipe making is performed by four-pass squeeze rolling, in which the furnace time is 3 to 4 hours and the extraction temperature is 1100 ° C., and then the oval hole type, round hole type, oval hole type, and round hole type are used for rolling down. Reduced diameter rolling was performed. At this time, the reduction ratio was adjusted to 1 to 2.5 in the oval hole type-round hole type of the former stage and the latter stage, respectively, and the total reduction ratio was adjusted to 1 (no pressure reduction) to 5.

  The steel slab obtained by the above-mentioned reheat reduction rolling is heated to 1250 to 1300 ° C., pierced and rolled using a Mannesmann piercing and rolling machine to form a hollow shell, and then immediately stretched by a mandrel mill. After reheating the resulting long element tube, it was made constant by a stretch reducer and finished to a finished dimension of outer diameter: 25.4 to 177.8 mm, thickness: 2.3 to 40 mm, and a 25 mm crop. After cutting, heat treatment was performed to obtain a product seamless steel pipe.

  The obtained product seamless steel pipe was subjected to an ultrasonic flaw detection test over the entire length thereof, and a pipe having an echo height at the inner surface exceeding the threshold was determined to be a defective pipe. The ratio of pipes with defects to the number of pipes produced was evaluated as the defect rate. The evaluation results are shown in Table 5. As is apparent from Table 5, according to the present invention, the defect rate can be reduced to 1/3 or less, and the maintenance after pipe making can be greatly reduced, so that yield improvement and cost reduction effects can be expected.

1: Continuous casting mold 2: Secondary cooling zone 3: Axial solidification early forced cooling zone 4: Axial solidification late forced cooling zone 5: Straightening zone S: Strand

Claims (5)

In continuous casting of high-Cr steel seamless steel pipe round slabs containing 12 to 18% Cr by mass ratio,
For a strand having a circular cross-section containing unsolidified molten steel inside in the process of continuous casting, following the secondary cooling, at least the axial solid phase ratio fs of the strand is 0.5 from the position where it becomes 0.2. From the position where the axial solid phase ratio fs becomes 0.5 after the axial solidification forcible cooling in the axial center in which the water density Q ₁ is 30 to 90 L / m ² / min is performed over the section. switch between reaching the a position, at least the fs is over a section from a position of 0.8 to axial center temperature of the strands is (Ts-145) ℃, the water density Q _2. 20 to 60 L / m ² / min and the water volume density Q ₂ is lower than the cooling water density Q _1E at the end of the forced cooling of the axial center solidification early stage solid phase late cooling is performed. Continuous casting of round slabs for making high Cr seamless steel pipes Method.
Here, the axial solid part ratio fs means the mass ratio of [solid phase / (solid phase + liquid phase)] in the strand axial part, and Ts is the solid phase of the molten steel used for continuous casting. Refers to the line temperature.   2. The high-Cr seamless steel pipe round tube according to claim 1, wherein the initial cooling of the axial center solidification is started at a position where the axial solid phase ratio fs is 0.01 to 0.2. A continuous casting method for slabs.   The continuous casting method for round slabs for high Cr seamless steel pipe pipe making according to claim 1 or 2, wherein the cooling water density density given in the axial solidification late forced cooling is reduced toward the downstream side of the strand. .   The high-chromium steel is a 13Cr steel containing 12.7 to 13.2% Cr by mass ratio, and the round slab for pipe making of high Cr seamless steel pipe according to any one of claims 1 to 3 Continuous casting method.   The diameter of the seamless steel pipe-made round cast slab is 170-330 mm, The continuous casting method of the high Cr seamless steel pipe-made round cast slab according to any one of claims 1-4.