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log K,P,fic = log {[Ti][C]} = 9.0- 10330/T’, where T is the temperature in Kelvin. Using this volubility product equation, the precipitation temperature in a Ti- New Approaches to the Design of ULC Sheet Steels M. Hua, C. I. Garcia, and A. J. DeArdo Basic Metals Processing Research Institute Department of Materials Science and Engineering University of Pittsburgh, Pittsburg~ PA 15261, USA (412) 624-8593 ABSTRACT The use of a new stabilization map, based on the observed precipitation behavior, allows for the rational design of ULC steels. The complete or partial stabilization of carbo~ and, flu-therrnore, the grain boundary composition of highly segregating elements, such as B, C and Nb, can be achieved through adjustment of the bulk composition. This diagram can be used to either analyze the behavior of existing steels or to design new high performance steels. 1. INTRODUCTION In recent decades, interstitial-free or ultra-low carbon (ULC) sheet steels have been widely used in the automobile industry, because of their good formability, especially deep drawing. The ULC steels are very flexible since they can be produced using either batch annealing or continuous annealing lines without strain aging or yield point phenomena. These steels are produced using vacuum degassing in steelmaking to reduce the contents of the interstitial elements C and N to about 30 ppm, which would then be stabilized by the addition of Ti and/or Nb. 14 This paper reviews the dependence of the carbon stabilization mechanism upon the composition of ULC steels and to illustrate the application of a newly- developed stabilization diagram for ULC steels. 2. STABILIZATION MAP The traditional view of stabilization results in the stabilization map, Figure 1, which may be applicable to microalloyed steels and ULC steels with low S and/or high Mn. The volubility product of TiC may be described as’ 40TH ,... only steel (Table I, steel Al) is estimated about 806 K (533”C), which is very low compared to the temperature for the formation of carbosulfide H phase. For steels whose composition are above the stoichiometric line (Ti*/C=4, Ti* = Tititil - 3 .42N+Nb/l .94), there is sufficient Ti to stabilize C. However, whether complete stabilization can actually be obtained is also dependent on having adequate kinetics. Hence, similar steels might exhibit different levels of stabilization when processed on different strip mills. Steels designed to fall into region 2 of Figure 1 would be bake hardenable, since the fi-ee carbon would be available for strengthening through strain aging when the steel is heated during the painting cycle.899 Furthermore, steels designed to fall into region 2 of Figure 1 can be fhrther stabilized through the addition of Nb. In this case, the Nb would act as a particle former in a manner similar to its behavior in conventional microalloyed steels. The present work suggests a new precipitation map to aid in the understanding of precipitation and stabilization in S-containing (0.004-0.1 Clwt pet.), low P (<0.02), low Mn (<0.2) ULC steels, Figure 2. The experimental basis for Figure 2 is that the formation of H phase is not by independent nucleation and growth, but rather by the in-situ transformation of TiS. 10-14 The major difference between Figures 1 and 2 is the zero point. In Figure 1, point Ti*=C=O represents, theoretically, the completion of TiN precipitation and the starting of TiC. In Figure 2, the “origin” for the formation of TiC is pushed back to a new point (Ti*=TiEF3 S, C=CH3 S/8). The slope of the stoichic}metric line is the same as in Figure 1, but this stoichiometric line starts at Ti*=l.5 S (C=O) since TiS forms before epitaxial carbides (TiC). and free standing carbides (TiC)~. When S=0, Figure 2 would degenerate into Figure 1. In the region I of Figure 2, which is above the stoichiometric line and C=CH, all the carbon can be stabilized by forming H- TiqC2Sz, Since H phase is much more stable than TiC (lower free energy of formation AG\ plus large particle size), the soluble C, which is in equilibrium with H, should be much lower than that with TiC. Therefore, the new mechanism indicates a better stabilization condition, or a real “interstitial-free” matrix. This is supported by the observation that high S levels can eliminate the bake hardenability or aging index of ULC steels.8’9’15 A recent experiment using internal friction also showed that a ULC steel in region V has 0.5 ppm C and 0.2 ppm N remaining in solution (not stabilized) in the hot rolled band material, while the residual C in steels of regions I and 11 is below the detection limit (about 0.1 ppm). 16 MWSP CONF. PROC., 1SS 1998 – 111 Ti o Fig sto the stab f. - volume fraction of preci Al A2 i r 1 I I C (ppm) 30 30 1 I N (ppm) I 30 I 30 S (ppm) I 80 I 80 Mn (ppm) I 15000 I 10000 Ti (ppm) 500 750 Nb (ppm) I I fv (TiN) 1.94X104 1.94X104 fv (H) 0.715X 104 f. (MC) 2.41x 10A 2.12X104 Fpi.*, MPa 0.5913 0.5430 I 1 ml (PPm) 1 - * using flexible boundary model, Fpt r~c = 5 nm, rH = 200 nm, 112 – 40TH MWSP CONF. PROC., 1SS pitates, ~] - Nb in solution A3 B c I I I 30 ~ 30 30 1 I I 30 I 30 I 30 I 80 I 80 I 80 I 15000 I 1000 I 400 103 500 223 I 250 I 300 I 432 I.94X104 1.94X104 1.94X104 5.94X104 6.22x104 2.65x104 0.6308 0.004 0.004 I I I 200 200 = 3 G f,m / (rcr), (ref. 20), and assuming TiN = 500 nm, and cr=O.8 J/mz. 998 1~.o1 Stabilizedpi] + TiC 41~c$$~*66,@o o2 Unstabilized*LO TiC + [C] c, Wt’%o ure 1. Traditional precipitation map. Above the ichiomettic line (Ti*/C=4, Ti*=Titil-3 .42N+0.5 lNb) re is sufficient Ti and the steel is generally considered as ilized by forming TiC. ? I II III Ti* Ti~ Ti* ok==== CH c, w pet Figure 2. Proposed precipitation map for S-containing, Ti stabilized ULC steels. Ti*=Tihtil - 3.42N (@us Nb/1 .94 only when TiS formed). The region II has epitaxial carbides (TiC)., whereas regions HI and IV have both (TiC)e and free-standing carbides (TiC)~. Ti*=l .5S is the amount of Ti needed to form TiS; Ti~3 S and Cm3S/8 stand for the maximum amount of Ti and C in H phase (TiiC2S2), respectively. Table I. Examples of Designed ULC Steel Compositions and Mass Balances Usually, the minimum bulk C content obtainable in a commercial ULC is fixed by steelmaking and the amount of S can be varied (e.g., to balance the C in forming the H phase). However, there should be an optimum (iv) ~] on cxferrite grain boundaries for amelioration of out bursting phenomena, T combination of S and Ti, even in the “stabilization zone”. If Ti is too high, some surface defects may result. I* It should be understood that, in order to make use of the stabilization mechanism proposed in Figure 2, the effects of other elements should also be taken into account. For example, Mn should be controlled to avoid the formation of MnS. Also, the addition of other elements must be viewed fi-om the standpoint of their effects on the stabilization diagram. For the Ti+Nb steel, Nb may be counted as ATi*=Nb/1 .94, but a minimum amount of Ti (e.g., Ti*=TiA) is needed such that TiS formation is insured, since Figure 2 is not valid for Nb- only ULC steel, as fhrther discussed below. Although Nb-only, Ti-only and Ti+Nb ULC steels are ~allcalled “interstitial free” steels, the mechanisms by which the stabilization of C occurs are often quite different. Stabilization in the Nb-only steel behaves like what is expected in a HSLA steel, that is, largely independent of the Mn and S contents of the steel, while in the Ti-containhg steel the stabilization of C depends upon the amount of Mn and S in the steel. Previous work revealed Nb-containing precipitates (in Ti+Nb ULC steel) only in the following conditions: 1) as-cast, which were produced by continuous casting,2) reheated below 1000”C and 3) TMP below 1000”C. Reheating or TMP above 1000”C resulted in the absence of Nb in the precipitates. 13 It follows that Nb does not have strong influence on the precipitation in filly Ti-stabilized steel. Therefore, the ‘effects of Nb on the behavior of the ULC steels, such as yield strength and ductility, lZ could then be explained by the amount of Nb in solution, rather than arguments based on precipitation. Furthermore, the major portion of the total Nb, found to be present in solution on the ferrite grain and subgrain boundaries, appears to be responsible for the stronger (557)[~ T9 5] textures and deep drawability found in the Nb-bearing stabilized steels.12 In addition, the Nb in solution has been confirmed to be responsible for the enhanced resistance to powdering, outbursting and cold work embrittlement ofien observed in single-stabilized Ti ULC steels. I* Therefore, the possible roles of Nb in ULC steels include: (i) intercalated TiS to (TiO.sNbO.s)dCzS*, (ii) ~] on cx ferrite grain boundaries for texture control, (iii) ~] on cx ferrite grain boundaries for CWE (cold work embrittlement) control, 40 (v) ~] on a ferrite grain boundaries for improved powdering resistance after galvannealing. From above discussion, the alloy design of fiture ULC steels may follow a different path, as will be discussed in sections 3B and 3C. Through better understanding of the physical metallurgy, fiu-ther improvement of these steels should be possible. 3. APPLICATION OF THE POLYPLOT As a result of new understanding of C stabilization in ULC steels, a computer simulation program (polyplot) has been developed to predict and analyze, for a given ULC steel composition, the stabilization condition in the hot band material and the microstructural behavior (such as pinning force for recrystallization and grain boundary composition) during hot rolling. 3.1 Traditional Approach to Alloy Design for Stabilization As previously mentioned, early alloy design was based on the stoichiometry of the particles TiN and TiC. Later, the carbosulfide TidC& was incorporated into the stabilization equation: Ti(total) = Ti(ex) + 3.43N + 4C + 1.5S. There had been several approaches based on these concepts as described below. Case I. Ti addition is intended for the formation of TiN and TiC through the reactions Ti + N = TiN, and Ti + C = TiC. This approach assumes that the nucleation and growth of precipitates take place independently and the alloy is considered as a dilute microalloyed steel. An example (Al) is shown in Table I. It should be pointed out that, in this case, the small precipitates (<5 nm, for example) may exert a pinning force sufficient to retard the recrystallization of the ferrite after cold rolling. Case II. Ti addition is intended for the formation of TiN, H and TiC through the assumed reactions Ti + N = TiN, 4Ti + 2S + 2C = TidC*Sz (H), and Ti + C = TiC. This approach assumes that the carbosulfide TidCN* (H-phase) was formed directly from the austenite, H MWSP CONF. PROC., 1SS 1998 – 113 4. suMMARYbut the ULC steel is still considered as a dilute microalloyed steel. An example (A2) is shown in Table I. Case III. Ti addition is intended for the formation of TiN and the Nb addition for NbC assuming the 98 It has been shown that there are two forms of following reactions Ti + N = TiN, and Nb+c=Nbc. This approach assumes that the nucleation and growth of precipitates takes place independently and the alloy was again considered to behave like a microalloyed steel. An example (A3) is shown in Table I. 3.2 New Approach to Alloy Design for Stabilization and Control of Grain Boundary Compositions Ti+Nb dual stabilized ULC steels, with the Ti addition intended for the formation of TiN and TiS and also to intercalated along with C the TiS to H. The Nb addition is intended for remaining in solution on the a ferrite grain bourldaries. The reactions involved are Ti + N = TiN, Ti + S = TiS, TiS + Ti + C = %Ti4CzSz, and ml= ml. It should be noted that in these ULC steels the nucleation and growth of H phase is not an independent process but an in-situ transformation and the alloy does not behave like a microalloyed steel. An example (B) is shown in Table 1. It should be pointed out that, in this case, the large precipitates (> 200 nm, for example) should not be enough to insert a pinning force to interact with the recrystallization process of the material. About 70°/0 of the total Nb is available for ferrite grain boundary segregation, which may lead to improvements in CWE and other properties. 3.3 Future Approach to Alloy Design for Stabilization and of Grain Boundary Compositions Ti addition is intended for the formation of TiN and TiS while Nb is intended for both the transformation from TiS to H and for being in solution on the ct ferrite grain boundaries. The reactions are Ti + N = TiN, Ti + S = TiS, TiS + Nb + C = %(Ti,Nb)dCzSz, and ml= ml. An example (C)is shown in Table I. 114 – 40TH MWSP CONF. PROC., 1SS 19 carbon stabilization in ULC steels. These are through the formation of MC carbides or by the formation of carbosulfides M.4C& The two approaches obviously differ in the role played by sulfhr. The stabilization reactions that actually occurs is dictated by the bulk composition of the steel. This behavior can be predicted through the use of a new stabilization diagram. The use of the stabilization diagram allows for the rational design of ULC steels. For example, the complete or partial stabilization of carbon can be achieved through adjustment of the bulk composition. Furthermore, this diagram can be used to control the grain boundary composition, which has been shown to be important in controlling the texture, galvannealing, powdering, and cold work embrittlement behavior in these steels. Titanium is usually considered as a precipitate former or C-stabilizer (when forming TiC and/or H). Niobium can act as stabilizer (when substituting Ti in forming NbC, MC and H) and/or grain boundary strengthener. ACKNOWLEDGEMENT We thank the University of Pittsburgh Interstitial Free Steel Consortium and the Basic Metals Research Institute, Department of Materials Science and Engineering, University of Pittsburgh, for sponsoring this work. REFERENCES 1. Metallurgy of Continuous-Annealed Sheet Steel, Bramfitt, B. L., and P. C. Mangonon, Jr., Editors, TMS-AIME, Warrendale, PA 1982. 2. Technology of Continuously Annealed Cold-Rolled Sheet Steel, Pradhan, R., Editor, TMS-AIME, Warrendale, PA 1985. 3. Metallurgy of Vacuum-Degassed Steel Products, Pradhan, R., Editor, TMS-AIME, Warrendale, PA 1990. 4. Interstitial Free Steel Sheet: Processing, Fabrication and Properties, Proc. Int. Sym., Edited by Collins, L. E., and D. L. Baragar, Canadian Institute of Mining, Metallurgy and Petroleum, Ottaw~ 1991. 5. International Forum for Physical Metallurgy of IF steels, The Iron and Steel Institute of Japan, and Nksho Iwai Corporation, Tokyo, 1994. 6. 7. 8. 9. Hook, R. E., and H. 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