GB2043103A

GB2043103A - Heat treating steel

Info

Publication number: GB2043103A
Application number: GB7937796A
Authority: GB
Original assignee: Ford Motor Co Ltd; Ford Motor Co
Current assignee: Ford Motor Co Ltd; Ford Motor Co
Priority date: 1978-11-02
Filing date: 1979-10-31
Publication date: 1980-10-01
Also published as: US4196025A

Description

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GB2 043103A

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SPECIFICATION

High strength dual phase steel

5 This invention relates to dual-phase steel.

The terms" dual-phase steel" are used to refer to a steel consisting essentially of a dispersion of martensite in a fine-grained ferrite matrix; these steels are of increasing tech-10 nological interest bacause they provide a better combination of strength and ductility than any other steel sheet material. The strength is important because it offers the opportunity to produce lighter components, while good duc-15 tility is needed to permit the easy forming of components. It is generally recognized that martensite plays a role in determining the strength level of dual-phase steels. A full understanding of the role played by the 20 phases in determining such characteristics needs to be more fully explored of how to maximize the martensite level of such steels while maintaining good ductility remains the subject of continued research in the industry. 25 There are currently two methods used to commercially produce dual-phase steels in the United States: (a) intercritical annealing requires the use of an annealing cycle wherein the steel is heated to the alpha + gamma 30 phase region (approximately 730-840T at .1 weight percent carbon) and is then cooled at a rate of less than 100°C per second. The austenite treatment involves controlling the cooling of the steel in the austenitized condi-35 tion during hot rolling so that the cooling rate is adjusted to promote the existance of both ferrite and martensite in the cooled product.

The chemical composition of the steel used to produce such dual-phase steels by either 40 method typically comprises . 1 % carbon, 1.4% manganese, .5% silicon, along with a singular addition of either .1% vanadium or .15% molybdenum or .4% chromium.

It has been discovered, with respect to this 45 invention that the strength of dual-phased steels is controlled essentially by the amount of martensite in the structure and that this relationship is linear. It has been further observed as part of this invention that not all of 50 the austenite transforms to martensite upon cooling by either of the methods above described. With intercritical annealing according to the prior art, one finds that additional ferrite and carbides are formed without a 55 complete conversion of all of the austenite to martensite. With respect to the austenitized dual-phase steels, a considerable amount of carbides are formed because the slow cooling path enters the region in which carbides are 60 formed. Therefore, there remains the technological problem of how to achieve an increased martensite content in a dual-phase steel without generation of carbides and to do so at a cooling rate which is less than 100°C 65 per second, a limitation imposed by the available equipment used in most steel mills today. It is well recognized that if cooling rates highly in excess of 100°C/sec., such as 1000°C/sec., were employed, there would be no difficulty in obtaining increased austenite conversion to martensite; but this alternative is not economically satisfactory.

SUMMARY OF THE INVENTION

The primary object of this invention is to provide an improved dual-phase steel having increased strength at higher ductility levels.

Another object is to provide an improved method of making dual-phase steels which method imparts increased hardenability to the austenite phase.

Yet another object of this invention is to provide an improved method of making a dual-phase steel which increases the ductility of such steel by increasing the strength level of the ferrite phase.

Detailed features pursuant to the above objects comprise: (a) regulating the chemistry of the steel to contain in addition to the normal ranges of manganese, carbon and silicon, the addition of synergistic elements consisting of .07-. 12 vanadium, .1-.2 molybdenum, and .3-.5% chromium, the latter combination of additive elements operating to synergistically suppress the transformation front of the steel in a manner to facilitate use of cooling rates of 100°C or less and insure substantial transformation of austenite to martensite; (b) controlling the grain size of the resulting dual-phase steel by the employment of a predetermined fine grain starting material having a grain size less than 10 microns; and (c) increasing the strength of the ferrite phase by the limitation of silicon to the range of .55-1.0%.

SUMMARY OF THE DRAWINGS

Figure 7 is a graphical illustration of flow stress as a function of quench temperature and carbon content for a series of vacuum cast dual-phase alloys containing 0.06-.29 carbon, 1.2-1.5 Mn, and the remainder Fe;

Figure 2 and 3 are graphical illustrations of flow stress at various strain levels as a function of percent martensite for the alloys of Fig. 1; and

Figure 4 is a graphical illustration of tensile strength as a function of annealing temperature for the alloys of Fig. 1-3 to which has been added various strengthening alloys.

DETAILED DESCRIPTION

Steels having structures consisting of mixtures of ferrite and martensite are often referred to as dual-phase steels, even through there are many commercial steels which have more than one phase. It has been shown that when a commercial SAE grade 980 XK H.S.L.A. steel is heat treated to produce the dual-phase structure, its yield point decreases

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GB2 043103A

(for example from 80 to 55 ksi), the total elongation increases from about 18 to 27%, while the tensile strength remains constant at approximately 95 ksi. The increase in ductility 5 and constant tensile strength leads to better formability and makes these dual-phase steels very attractive for use in cold formed high strength components.

It is surprising to find from a study of dual-10 phase structures that strength is a linear function of the percent martensite. This is surprising since the martensite content was varied by changing the quenching temperature, and therefore the carbon content of the marten-1 5 site. The strength of martensite should be presumably very carbon dependent. Turning to Fig. 1, it plots flow stress as a function of quench temperature and carbon content of the alloy for a series of vacuum cast alloys 20 containing .06-.29 carbon, 1.20-1.50 manganese and the remainder iron. It can be seen that, at a given quench temperature, flow stress is linearly dependent upon the carbon content and that, at a given carbon level, the 25 higher the quench temperature the larger the flow stress.

Data with respect to flow stress at various strain levels as a function of percent martensite is presented in Figs. 2 and 3. It is clear 30 from these figures that all the flow stresses are solely the function of the percent of martensite in the alloy and do no depend upon the carbon content of martensite. This is an unexpected result because from the laws of 35 simple mechanical mixture, it would be predicted that the flow stress of the alloys quenched from 740°C (carbon content in martensite is approximately .57%) should be measurably stronger than alloys quenched 40 from 800°C (carbon content .38). Moreover, martensite strength is known to be very sensitive to such changes in carbon content.

With this relationship in mind, it is a goal of this invention to provide a more complete 45 transformation of all of the austenite to martensite in order to achieve a maximum strength level. However, the state of the art is not capable of insuring that all of the austenite, that is generated by intercritically anneal-50 ing a steel prepared for dual-phase production, will transform fully to a martensite plug ferrite product. It is known that some alloy additions tend generally to delay the start of transformation to a limited degree and to 55 increase the time for its completion. The importance of this is that in a transformation diagram, plotting temperature versus time, the zone in which certain transformation products occur can be easily depicted. It is desirable 60 that the line or front representing the initiation of transformation products be suppressed and that the line be displaced to the right. In this way, transformation at all temperature levels will start later and is slower to go to comple-65 tion, thereby upon cooling intercritically annealed steel, it would be more convenient and easier to obtain increased volume fraction of martensite by bypassing such transformation front.

70 Unfortunately, the state of the art is not capable of completely bypassing this transformation front at cooling rates of 100°C or slower to achieve greater conversion to martensite; some austenite will transform back to 75 ferrite in dual-phase steels that are produced by the intercritical anneal (this invention is not concerned with steel made by an austenite treatment since such steels inherently contain carbides detrimental to the ultimate strength 80 of the steel.

As an example of the state of the art, it is readily known that small additions of vanadium or chromium will facilitate an increase in the strength of a dual-phase steel. The effect 85 of the alloying element employed differs greatly both in magnitude and effect in different temperature regions so that the precise strength prediction of a given alloy combination is not quite possible. The prior art has 90 employed small quantities of vanadium or chromium in the production of dual-phased steels. The net result of this is displayed in Fig. 4, wherein employing a variety of intercritical annealing temperatures from 95 760-820°C, the tensile strength for a .1% vanadium steel remains just below 100 ski. With 5% chromium, the strength level remains substantially at 105 ski when employing annealing temperature between 100 760-800°C, but at 820°C the strength level is slightly elevated to 120 ksi.

It is the discovery of this invention that by employing ,1-.20% molybdenum, particularly in combination with .07-.2% vanadium and 105 .3-.5% chromium, a dramatic synergistic effect takes places which insures that considerably more of the austenite which is generated upon heating to the intercritical range will be converted to martensite upon cooling at rates 110 of 100°C or less. These particular chemical ingredients remove interstitial atoms'from the ferrite matrix during the production of these dual-phase steels. Only by providing a completely interstitially free matrix can there occur 115 the optimum combination of strength and ductility which is achieved by the highest conversion of austenite to martensite. To prove this effect, a series of alloy ingots were prepared by vaccum melting with a base 120 composition consisting of (by weight percent) .11 carbon, 1.4 manganese and .55 silicon. To this was added singly and in all combinations of 0.1 vanadium, .2 molybdenum/or .5 chromium. The ingots were hot rolled to sheet 125 form having a thickness of approximately .1 inch. Tensile specimens were prepared directly from this hot rolled material by cutting sections 2 X .5 inches. A ferrite grain size of about 10 microns was obtained by annealing 130 the hot rolled product separately, but this is

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normally provided by control of the grain size during hot rolling. The dual-phase structure was produced by annealing at temperatures between 760 and 820°C, (the insensitive por-5 tion of the intercritical annealing range) for 8 minutes, the increments of temperature levels for the different specimens being demonstrated in Fig. 4. Cooling from the intercritical annealing temperature was carried out to 10 room temperature in forced air at a rate of about 30°C per second. The tensile specimens resulting from such heat treatment were tested in an Instron machine at room temperature at a cross head rate of approximately 15 2 X 10-2 mm/s (0.05 in./min.)

The synergism effect is most evident when the specimen, containing only .1% V as the additive to the base manganese-carbon-iron alloy, is considered. It possessed a tensile 20 strength of about 100 KSI from data illustrated in Fig. 4. When chroimum is employed as the only additive to the base manganese-carbon-iron alloy, a tensile strength of about 105 ksi is obtained, a difference of 5 ksi over 25 the vanadium steel. When both vanadium and chromium are combined as the additives, a tensile strength of about 1 20 ksi is obtained an increment of 15 ksi over the steel with only chromium. When vanadium, chromium, 30 and molybdenum are combined as the additive, a tensile strength of about 150 ksi is obtained at annealing temperatures of 760-800°C, an increment of 30 ksi over the chromium-vanadium additive steel. Similarly 35 the combining of molybdenum with either chromium (rendering a tensile strength of about 140 ksi) or vanadium (rendering a tensile strength of about 130 ksi) is a significant increment over the use of chromium by 40 itself (about 105 ksi) or vanadium by itself (about 100 ksi).

Grain size plays an important role with respect to achieving the best combination of strength and ductility. To this end, the use of 45 a known grain refining element (niobium) was investigated. The grain refinement observed in the dual-phase structure was in general a reflection of the grain refinement that took place in the austenite during hot rolling of the 50 steel ingot. Micrographs of these alloys after i quenching from 760°C, confirm that niobium additions resulted in a finer grain size and the higher manganese level, particularly in the presence of niobium, produced the best grain 55 refinement. The strength of test alloys as a function of quench temperature can be understood in terms of varying martensite content and grain size. Alloys having comparable grain sizes and martensite contents will have 60 their strengths about the same, while alloys having similar martensite contents but with different grain sizes will have different strength levels. It is concluded that to maximize the ductility in combination with the 65 strength of dual-phase steel, the ferrite phase should possess a fine grain size to make the ferrite of greater strength and be free of fine precipitates and interstitial alloying elements. Grain refinement is principally a matter of 70 proper rolling techniques, including a proper sequence of incremental thickness reductions at correspondingly lower temperature levels for each successive reduction, such as exemplified in making, shaping and treating of 75 steel, published by U.S. Steel Corp., chapter 44. With such rolling techniques, the appropriate grain size of less than 10 microns can be assured.

In addition, solid solution strengthening can 80 be achieved by use of silicon as a substitutional strengthener of iron. It has been found that between .55-1.0% silicon increases the uniform elongation of ferrite at a constant yield stress; this effect is especially pro-85 nounced at low temperatures.

By utilizing both the synergistic effect from a combined vanadium-chromium-molybdenum addition, and prior grain refinement (3-7 microns), a unique dual-phase composition at 90 the thickness of .25 inches or less results which is characterized by about 30% volume fraction of martensite uniformly dispersed throughout a fine grained ferrite matrix devoid of carbon.

95 The composition exhibits an elongation of at least 14% at a tensile strength level of 140 ksi and 1 2% at 1 50 ksi. The total alloying ingredients selected from V, Mo and Cr,

should be no greater than .8%, the individual

100 ranges for said elements being 0-1.15 vanadium, .3-.5 chromium, and .1-.02 molybdenum.

The ferrite matrix is substantially interstiti-ally free, devoid of carbides, and characterized

105 by a strength level of 55 ksi at a grain size of 5-10 microns. Relatively speaking, the ferrite matrix is soft (having a Brinnell value of 100), compared to the martensite phase (having a Brinnell hardness level in excess of 400).

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Claims

1. A hot-formed dual-phase sheet steel composition, consisting of .05-1.15 carbon, .25-1.0 silicon, .55-1.6 manganese, 0-.15

115 vanadium, .1-.02 molybdenum and .3-.5 chromium, the remainder iron, said composition being particularly characterized by about 30% volume fraction of martensite uniformly dispersed throughout a fine grained ferrite

120 matrix devoid of carbon, said composition exhibiting an elongation of at least 14% at a tensile strength level of 140 ksi and 12% at 150 ksi.

2. The composition as in Claim 1, in

1 25 which the total content of alloying ingredients selected from vanadium, molybdenum and chromium is no greater than .8%.

3. The composition as in Claim 1, in which the ferrite matrix is substantially inter-

130 stitially free.

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4. The composition as in Claim 1, in which the ferrite matrix is characterized by a strength level of 55 ksi with a grain size of 5-10 microns.

5 5. The composition as in Claim 1 in which the thickness of said sheet steel composition is limited to 1/4 inch or less.

6. The composition as in Claim 1, in which the grain size of said ferrite matrix is

10 3-7 microns.

7. The composition as in Claim 1 in which said matrix is devoid of fine carbides.

8. The composition as in Claim 1, in which said ferrite is soft having a ductility

1 5 level of Brinnell 100 and said martensite is relatively hard having a hardness level in excess of Brinnel 400.

9. A method of making a dual-phase steel comprising:

20 (a) hot-forming a flat rolled steel product consisting essentially of, by weight, .05-.15% carbon, .25-1.0% silicon, 1.2-1.6% manganese, 0.1-.2% vanadium, .1-12% molybdenum and .3-.5% chrom-

25 ium.

(b) heat said product to the insensitive portion of the intercritical annealing temperature range generally equivalent to 740-830°C, permitting the carbon of said steel to be

30 segregated in solution so as to be constituted for dual-phase comprised of austenite and ferrite, said austenite constituting 30-40% by volume of said heated product,

(c) cooling said heat product at a rate of

35 less than 100°C per second to room temperature to convert substantially all of the austenite to martensite, the heat treated product being characterized by a strength level of at least 140 ksi and an elongation of at least

40 12%.

10. The method as in Claim 9, in which the flat rolled steel is controlled to a thickness of V4 inch or less to avoid a transformation product gradient.

45 11. The method as in Claim 9, in which the hot forming step is carried out in a series of reduction stages at progessively lower temperature to produce a grain size of 3-7 microns.

Printed for Her Majesty's Stationery Office by Burgess & Son (Abingdon) Ltd.—1980.

Published at The Patent Office, 25 Southampton Buildings,

London. WC2A 1AY, from which copies may be obtained.