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Here is a collection of articles about iron properties, using iron and how to design iron for manufacturing purposes.

The views that are expressed in these articles are not to be considered the views of Intercast and Forge.

Designing with ductile iron
The Casting Advantage
Design Flexibility
Reduced Costs
Materials Advantages
Cast Iron:  The Natural Composite
Types of Cast Irons
History of Ductile Iron
The Ductile Iron Advantage
The Ductile Iron Family
A Matter of Confidence
References

Gray Iron - A Unique Engineering Material
Metallurgy of Gray Iron
Composition
Effect of Section Size on Structure
Casting Processes
Casting Design
Mechanical Properties of Gray Iron
Heat Treatment of Gray Iron
Machining of Gray Iron
The Future for Gray Iron
References


Designing with ductile iron
By Dr. Richard Warda, QIT and CANMET

The Casting Advantage
The casting process has been used for over 5000 years to produce both objects of art and
utilitarian items essential for the varied activities of civilization. Why have castings played such a significant role in man's diverse activities? For the artist, the casting process has provided a medium of expression which not only imposed no restrictions on shape, but also faithfully replicated every detail of his work, no matter how intricate. Designers use the same freedom of form and replication of detail to meet the basic goal of industrial design - the matching of form to function to optimize component performance. In addition to design flexibility, the casting process offers significant advantages in cost and materials selection and performance.
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Design Flexibility
The design flexibility offered by the casting process far exceeds that of any other process used for the production of engineering components. This flexibility enables the design engineer to match the design of the component to its function. Metal can be placed where it is required to optimize the load carrying capacity of the part, and can be removed from unstressed areas to reduce weight. Changes in cross-section can be streamlined to reduce stress concentrations. The result? Both initial and life-cycle costs are reduced through material and energy conservation and increased component performance.

Designer engineers can now optimize casting shape and performance with increased speed and confidence. Recent developments in CAD/CAM, solid modelling and finite element analysis (FEA) techniques permit highly accurate analyses of stress distributions and component deflections under simulated operating conditions. In addition to enhancing functional design, the analytical capabilities of CAD/CAM have enabled foundry engineers to maximum casting integrity and reduce production costs through the optimization of solidification behaviour.
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Reduced Costs
Castings offer cost advantages over fabrications and forgings over a wide range of production rates, component size and design complexity. The mechanization and automation of casting processes have substantially reduced the cost of high volume castings, while new and innovative techniques such as the use of styrofoam patterns and CAD/CAM pattern production have dramatically reduced both development times and costs for prototype and short-run castings. As confidence in FEA techniques increases, the importance of prototypes, often in the form of fabrications which "compromise" the final design, will decrease and more and more new components will go directly from the design stage to the production casting. As shown in Figure 2. 1, as component size and complexity increase, the cost per unit of weight of fabricated components can rise rapidly, while those of castings can actually decrease due to the improved castability and higher yield of larger castings. Near net shape casting processes and casting surface finishes in the range 50-500 microinches minimize component production costs by reducing or eliminating machining operations.

Replacement of a multi-part, welded and/or fastened assembly by a casting offers significant savings in production costs. Inventory costs are reduced, close-tolerance machining required to fit parts together is eliminated, assembly errors cannot occur, and engineering, inspection and administrative costs related to multi-part assemblies are reduced significantly. A recent study by the National Center for Manufacturing Sciences (NCMS) has shown that in certain machine tool applications, the replacement of fabricated structures by Ductile Iron castings could result in cost savings of 39-50%. Commenting on the NCMS study, Mr. Gary Lunger, President of Erie Press Inc., stated:

"We make huge presses and we have relatively clear specifications for what goes into each press. We have been able to use Ductile Iron as a substitute material primarily for cylinders and other parts at a significant cost saving over cast or fabricated steel."
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Materials Advantages
Castings offer advantages over forgings in isotropy of properties and over fabrications in both isotropy and homogeneity. The deformation processes used to produce forgings and plate for fabrications produce laminations which can result in a significant reduction in properties in a direction transverse to the lamination. In fabricated components, design complexity is usually achieved by the welding of plate or other wrought shapes. This method of construction can reduce component performance in two ways. First, material shape limitations often produce sharp corners which increase stress concentrations, and second, the point of shape change and stress concentration is often a weld, with related possibilities for material weakness and stress-raising defects. Figure 2.2 shows the results of stress analysis of an acrylic joint model in which the stress concentration factor for the weld is substantially higher than for a casting profiled to minimize stress concentration.
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Cast Iron: The Natural Composite
Iron castings, as objects of art, weapons of war, or in more utilitarian forms, have been produced for more than 2000 years. As a commercial process, the production of iron castings probably has no equal for longevity, success or impact on our society. In a sense, the iron foundry industry produces an invisible yet vital product, since most iron castings are further processed, assembled, and then incorporated as components of other machinery, equipment, and consumer items.

The term "cast iron" refers not to a single material, but to a family of materials whose major constituent is iron, with important amounts of carbon and silicon, as shown in Figure 2.3. Cast irons are natural composite materials whose properties are determined by their microstructures - the stable and metastable phases formed during solidification or subsequent heat treatment. The major microstructural constituents of cast irons are: the chemical and morphological forms taken by carbon, and the continuous metal matrix in which the carbon and/or carbide are dispersed. The following important microstructural components are found in cast irons.

Graphite
This is the stable form of pure carbon in cast iron. Its important physical properties are low density, low hardness and high thermal conductivity and lubricity. Graphite shape, which can range from flake to spherical, plays a significant role in determining the mechanical properties of cast irons. Figures 2.4 and 2.5 show that graphite flakes act like cracks in the iron matrix, while graphite spheroids act like "crackarresters", giving the respective irons dramatically different mechanical properties.

Carbide
Carbide, or cementite, is an extremely hard, brittle compound of carbon with either iron or strong carbide forming elements, such as chromium, vanadium or molybdenum. Massive carbides increase the wear resistance of cast iron, but make it brittle and very difficult to machine. Dispersed carbides in either lamellar or spherical forms play in important role in providing strength and wear resistance in as-cast pearlitic and heat-treated irons.

Ferrite
This is the purest iron phase in a cast iron. In conventional Ductile Iron ferrite produces lower strength and hardness, but high ductility and toughness. In Austempered Ductile Iron (ADI), extremely fine-grained accicular ferrite provides an exceptional combination of high strength with good ductility and toughness.

Pearlite
Pearlite, produced by a eutectoid reaction, is an intimate mixture of lamellar cementite in a matrix of ferrite. A common constituent of cast irons, pearlite provides a combination of higher strength and with a corresponding reduction in ductility which meets the requirements of many engineering applications.

Martensite
Martensite is a supersaturated solid solution of carbon in iron produced by rapid cooling. In the untempered condition it is very hard and brittle.  Martensite is normally "tempered" - heat treated to reduce its carbon content by the precipitation of carbides - to provide a controlled combination of high strength and wear resistance.

Austenite
Normally a high temperature phase consisting of carbon dissolved in iron, it can exist at room temperature in austenitic and austempered cast irons. In austenitic irons, austenite is stabilized by nickel in the range 18-36%. In austempered irons, austenite is produced by a combination of rapid cooling which suppresses the formation of pearlite and the supersaturation of carbon during austempering, which depresses the start of the austenite-to-martensite transformation far below room temperature. In austenitic irons, the austenite matrix provides ductility and toughness at all temperatures, corrosion resistance and good high temperature proper-ties, especially under thermal cycling conditions. In austempered Ductile Iron stabilized austenite, in volume fractions up to 40% in lower strength grades, improves toughness and ductility and response to surface treatments such as fillet rolling.

Bainite
Bainite is a mixture of ferrite and carbide, which is produced by alloying or heat treatment.
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Types of Cast Irons
The presence of trace elements, the addition of alloying elements, the modification of solidification behaviour, and heat treatment after solidification are used to change the microstructure of cast iron to produce the desired mechanical properties in the following common types of cast iron.

White Iron
White Iron is fully carbidic in its final form. The presence of different carbides, produced by alloying, makes White Iron extremely hard and abrasion resistant but very brittle.

Gray Iron
Gray Iron is by far the oldest and most common form of cast iron. As a result, it is assumed by many to be the only form of cast iron and the terms "cast iron" and "gray iron" are used interchangeably.  Gray Iron, named because its fracture has a gray appearance, consists of carbon in the form of flake graphite in a matrix consisting of ferrite, pearlite or a mixture of the two. The fluidity of liquid gray iron, and its expansion during solidification due to the formation of graphite, have made this metal ideal for the economical production of shrinkage-free, intricate castings such as motor blocks.

The flake-like shape of graphite in Gray Iron, see Figure 2.4, exerts a dominant influence on its mechanical properties. The graphite flakes can act as stress raisers which may prematurely cause localized plastic flow at low stresses, and initiate fracture in the matrix at higher stresses. As a result, Gray Iron exhibits no elastic behaviour and fails in tension without significant plastic deformation. The presence of graphite flakes also gives Gray Iron excellent machinability, damping characteristics and self-lubricating properties.

Malleable Iron
Unlike Gray and Ductile Iron, Malleable Iron is cast as a carbidic or white iron and an annealing or "malleablizing" heat treatment is required to convert the carbide into graphite. The microstructure of Malleable Iron consists of irregularly shaped nodules of graphite called "temper carbon" in a matrix of ferrite and/or pearlite. The presence of graphite in a more compact or sphere-like form gives Malleable Iron ductility and strength almost equal to cast, low-carbon steel. The formation of carbide during solidification results in the conventional shrinkage behaviour of Malleable Iron and the need for larger feed metal reservoirs, causing reduced casting yield and increased production costs.
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History of Ductile Iron Development
In spite of the progress achieved during the first half of this century in the development of Gray and Malleable Irons, foundrymen continued to search for the ideal cast iron - an as-cast "gray iron" with mechanical properties equal or superior to Malleable Iron. J.W. Bolton, speaking at the 1943 Convention of the American Foundrymen's Society (AFS), made the following statements.

"Your indulgence is requested to permit the posing of one question. Will real control of graphite shape be realized in gray iron? Visualize a material, possessing (as-cast) graphite flakes or groupings resembling those of malleable iron instead of elongated flakes."

A few weeks later, in the International Nickel Company Research Laboratory, Keith Dwight Millis made a ladle addition of magnesium (as a copper-magnesium alloy) to cast iron and justified Bolton's optimism - the solidified castings contained not flakes, but nearly perfect spheres of graphite. Ductile Iron was born!

Five years later, at the 1948 AFS Convention, Henton Morrogh of the British Cast Iron Research Association announced the successful production of spherical graphite in hypereutectic gray iron by the addition of small amounts of cerium.

At the time of Morrogh's presentation, the International Nickel Company revealed their development, starting with Millis' discovery in 1943, of magnesium as a graphite spherodizer. On October 25, 1949, patent 2,486,760 was granted to the International Nickel Company, assigned to Keith D. Millis, Albert P. Gegnebin and Norman B. Pilling. This was the official birth of Ductile Iron, and, as shown in Figure 2.6, the beginning of 40 years of continual growth worldwide, in spite of recessions and changes in materials technology and usage. What are the reasons for this growth rate, which is especially phenomenal, compared to other ferrous castings?
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The Ductile Iron Advantage
The advantages of Ductile Iron which have led to its success are numerous, but they can be summarized easily - versatility, and higher performance at lower cost. As illustrated in Figure 2.7, other members of the ferrous casting family may have individual properties which might make them the material of choice in some applications, but none have the versatility of Ductile Iron, which often provides the designer with the best combination of overall properties. This versatility is especially evident in the area of mechanical properties where Ductile Iron offers the designer the option of choosing high ductility, with grades guaranteeing more than 18% elongation, or high strength, with tensile strengths exceeding 120 ksi (825 MPa). Austempered Ductile Iron (ADI), offers even greater mechanical properties and wear resistance, providing tensile strengths exceeding 230 ksi (1600 MPa).

In addition to the cost advantages offered by all castings, Ductile Iron, when compared  to steel and Malleable Iron castings, also offers further cost savings. Like most commercial cast metals, steel and Malleable Iron decrease in volume during solidification, and as a result, require attached reservoirs (feeders or risers) of liquid metal to offset the shrinkage and prevent the formation of internal or external shrinkage defects. The formation of graphite during solidification causes an internal expansion of Ductile Iron as it solidifies and as a result, it may be cast free of significant shrinkage defects either with feeders that are much smaller than those used for Malleable Iron and steel or, in the case of large castings produced in rigid molds, without the use of feeders. The reduction or elimination of feeders can only be obtained in correctly design castings. This reduced requirement for feed metal increases the productivity of Ductile Iron and reduces its material and energy requirements, resulting in substantial cost savings. The use of the most common grades of Ductile Iron "as-cast" eliminates heat treatment costs, offering a further advantage.
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The Ductile Iron Family
Ductile Iron is not a single material, but a family of materials offering a wide range of properties obtained through microstructure control. The common feature that all Ductile Irons share is the roughly spherical shape of the graphite nodules. As shown in Figure 2.5, these nodules act as "crack-arresters and make Ductile Iron "ductile". This feature is essential to the quality and consistency of Ductile Iron, and is measured and controlled with a high degree of assurance by competent Ductile Iron foundries. With a high percentage of graphite nodules present in the structure, mechanical properties are determined by the Ductile Iron matrix. Figure 2.8 shows the relationship between microstructure and tensile strength over a wide range of properties. The importance of matrix in controlling mechanical properties is emphasized by the use of matrix names to designate the following types of Ductile Iron.

Ferritic Ductile Iron
Graphite spheroids in a matrix of ferrite provides an iron with good ductility and impact resistance and with a tensile and yield strength equivalent to a low carbon steel. Ferritic Ductile Iron can be produced "as-cast" but may be given an annealing heat treatment to assure maximum ductility and low temperature toughness.

Ferritic Pearlitic Ductile Iron
These are  the most common grade of Ductile Iron and are normally produced in the "as cast" condition.  The graphite spheroids are in a matrix containing both ferrite and pearlite.  Properties are intermediate between ferritic and pearlitic grades, with good machinability and low production costs.

Pearlitic Ductile Iron
Graphite spheroids in a matrix of pearlite result in an iron with high strength, good wear resistance, and moderate ductility and impact resistance. Machinability is also superior to steels of comparable physical properties.

The preceding three types of Ductile Iron are the most common and are usually used in the as-cast condition, but Ductile Iron can be also be alloyed and/or heat treated to provide the following grades for a wide variety of additional applications.

Martensitic Ductile Iron
Using sufficient alloy additions to prevent pearlite formation, and a quench-and-temper heat treatment produces this type of Ductile Iron.  The resultant tempered martensite matrix develops very high strength and wear resistance but with lower levels of ductility and toughness.

Bainitic Ductile Iron
This grade can be obtained through alloying and/or by heat treatment to produce a hard, wear resistant material.

Austenitic Ductile Iron
Alloyed to produce an austenitic matrix, this Ductile Iron offers good corrosion and oxidation resistance, good magnetic properties, and good strength and dimensional stability at elevated temperatures. The unique properties of Austenitic Ductile Irons are treated in detail in Section V.

Austempered Ductile Iron (ADI)
ADI, the most recent addition to the Ductile Iron family, is a sub-group of Ductile Irons produced by giving conventional Ductile Iron a special austempering heat treatment. Nearly twice as strong as pearlitic Ductile Iron, ADI still retains high elongation and toughness. This combination provides a material with superior wear resistance and fatigue strength. (See Section IV).
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A Matter of Confidence
The automotive industry has expressed its confidence in Ductile Iron through the extensive use of this material in safety related components such as steering knuckles and brake calipers. These and other automotive applications, many of which are used "as-cast", are shown in Figure 2.9. One of the most critical materials applications in the world is in containers for the storage and transportation of nuclear wastes. The Ductile Iron nuclear waste container shown in Figure 2.10  is another example of the ability of Ductile Iron to meet and surpass even the most critical qualification tests for materials performance.  These figures show the wide variety of parts produced in Ductile Iron.   The weight range of possible castings can be from less than one ounce (28 grams) to more than 200 tons.  Section size can be as small as 2 mm to more than 20 inches (1/2 meter) in thickness.
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References
S. Jeffreys, "Finite Element Analysis - Doing Away with Prototypes", Industrial Computing, September, 1988, pp 34-36.

"NCMS Study Reveals DI Castings May Mean Cost Savings." Modem Casting, May, 1990, p 12.

Jay Janowak, "The Grid Method of Cast Iron Selection". Casting Design and Application, Winter 1990, pp 55-59.

D. P. Kanicki, "Marketing of Ductile Iron," Modern Casting, April, 1988.

A Design Engineer's Digest of Ductil2 Iron, 5th Edition, 1983, QIT-Fer et Titane Inc., Montreal, Quebec, Canada.

S. I. Karsay, Ductile Iron II, Quebec Iron and Titanium Corporation, 1972.

B. L. Simpson, History of the Metalcasting Industry, American Foundrymen's Society.
Des Plaines, IL, 1969.

H. Bornstein, "Progress in Iron Castings", The Charles Edgar Hoyt Lecture,
Transactions of the American Foundrymen's Society, 1957, vol 65, p 7.

G.J. Marston "Better cast than fabricated", The Foundryman, March 1990, 108-113.

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Gray Iron-A Unique Engineering Material
by D. E. Krause
The Iron Casting Research Institute

Gray iron is the most versatile of all foundry metals. The high carbon content is responsible for ease of melting and casting in the foundry and for ease of machining in subsequent manufacturing. The low degree or absence of shrinkage and high fluidity provide maximum freedom of design for the engineer. By suitable adjustment in composition and selection of casting method, tensile strength can be varied from less than 20,000 psi to over 60,000 psi and hardness from 100 to 300 BHN in the as-cast condition. By subsequent heat treatment, the hardness can be increased to H Rc 60.

If the service life of a gray iron part is considered to be too short, the design of the casting should be carefully reviewed before specifying a higher strength and hardness grade of iron. An unnecessary increase in strength and hardness may increase the cost of the casting as well as increase the cost of machining through lower machining rates. Although the relationship between Brinell hardness and tensile strength for gray iron is not constant, data are shown which will allow use of the Brinell hardness test to estimate the minimum tensile strength of the iron in a casting.

Gray iron is one of the oldest cast ferrous products. In spite of competition from newer materials and their energetic promotion, gray iron is still used for those applications where its properties have proved it to be the most suitable material available. Next to wrought steel, gray iron is the most widely used metallic material for engineering purposes. For 1967, production of gray iron castings was over 14 million tons, or about two and one-half times the volume of all other types of castings combined. There are several reasons for its popularity and widespread use. It has a number of desirable characteristics not possessed by any other metal and yet is among the cheapest of ferrous materials available to the engineer. Gray iron castings are readily available in nearly all industrial areas and can be produced in foundries representing comparatively modest investments. It is the purpose of this paper to bring to your attention the characteristics of gray iron which make the material so useful.

Gray iron is one of the most easily cast of all metals in the foundry. It has the lowest pouring temperature of the ferrous metals, which is reflected in its high fluidity and its ability to be cast into intricate shapes. As a result of a peculiarity during final stages of solidification, it has very low and, in some cases, no liquid to solid shrinkage so that sound castings are readily obtainable. For the majority of applications, gray iron is used in its as-cast condition, thus simplifying production. Gray iron has excellent machining qualities producing easily disposed of chips and yielding a surface with excellent wear characteristics. The resistance of gray iron to scoring and galling with proper matrix and graphite structure is universally recognized.

Gray iron castings can be produced by virtually any well-known foundry process. Surprisingly enough, in spite of gray iron being an old material and widely used in engineering construction, the metallurgy of the material has not been clearly understood until comparatively recent times. The mechanical properties of gray iron are not only determined by composition but also greatly influenced by foundry practice, particularly cooling rate in the casting. All of the carbon in gray iron, other than that combined with iron to form pearlite in the matrix, is present as graphite in the form of flakes of varying size and shape. It is the presence of these flakes formed on solidification which characterize gray iron. The presence of these flakes also imparts most of the desirable properties to gray iron.
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Metallurgy of Gray Iron
MacKenzie[1] in his l944 Howe Memorial Lecture referred to cast iron as "steel plus graphite." Although this simple definition still applies, the properties of gray iron are affected by the amount of graphite present as well as the shape, size, and distribution of the graphite flakes. Although the matrix resembles steel, the silicon content is generally higher than for cast steels, and the higher silicon content together with cooling rate influences the amount of carbon in the matrix. Gray iron belongs to a family of high-carbon silicon alloys which include malleable and nodular irons. With the exception of magnesium or other nodularizing elements in nodular iron, it is possible through variations in melting and foundry practice to produce all three materials from the same composition. In spite of the widespread use of gray iron, the metallurgy of it is not clearly understood by many users and even producers of the material. One of the first and most complete discussions of the mechanism of solidification of cast irons was presented in 1946 by Boyles[2]. Detailed discussions of the metallurgy of gray iron may be found in readily available handbooks[3-7]. The most recent review of cast iron metallurgy and the formation of graphite is one by Wieser et al[8]. To avoid unnecessary duplication of information, only the more essential features of the metallurgy of gray iron will be discussed here.
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Composition
Gray iron is commercially produced over a wide range of compositions. Foundries meeting the same specifications may use different compositions to take advantage of lower cost raw materials locally available and the general nature of the type of castings produced in the foundry. For these reasons, inclusion of chemical composition in purchase specifications for castings should be avoided unless essential to the application. The range of compositions which one may find in gray iron castings is as follows: total carbon, 2.75 to 4.00 percent; silicon, 0.75 to 3.00 percent; manganese, 0.25 to 1.50 percent; sulfur, 0.02 to 0.20 percent; phosphorus, 0.02 to 0.75 percent. One or more of the following alloying elements may be present in varying amounts: molybdenum, copper, nickel, vanadium, titanium, tin, antimony, and chromium. Nitrogen is generally present in the range of 20 to 92 ppm.

The concentration of some elements may exceed the limits shown above, but generally the ranges are less than shown.

Carbon is by far the most important element in gray iron. With the exception of the carbon in the pearlite of the matrix, the carbon is present as graphite. The graphite is present in flake form and as such greatly reduces the tensile strength of the matrix. It is possible to produce all grades of iron of ASTM Specification for Gray Iron Castings (A 48-64) by merely adjusting the carbon and silicon content of the iron. It would be impossible to produce gray iron without an appropriate amount of silicon being present. The addition of silicon reduces the solubility of carbon in iron and also decreases the carbon content of the eutectic. The eutectic of iron and carbon is about 4.3 percent. The addition of each 1.00 percent silicon reduces the amount of carbon in the eutectic by 0.33 percent. Since carbon and silicon are the two principal elements in gray iron, the combined effect of these elements in the form of percent carbon plus 1/s percent silicon is termed carbon equivalent (CE). Gray irons having a carbon equivalent value of less than 4.3 percent are designated hypoeutectic irons, and those with more than 4.3 percent carbon equivalent are called hypereutectic irons. For hypoeutectic irons in the automotive and allied industries, each 0.10 percent increase in carbon equivalent value decreases the tensile strength by about 2700 psi.

If the cooling or solidification rate is too great for the carbon equivalent value selected. the iron may freeze in the iron-iron carbide metastable system rather than the stable iron-graphite system, which results in hard or chilled edges on castings. The carbon equivalent value may be varied by changing either or both the carbon and silicon content. Increasing the silicon content has a greater effect on reduction of hard edges than increasing the carbon content to the same carbon equivalent value. Silicon has other effects than changing the carbon content of the eutectic. Increasing the silicon content decreases the carbon content of the pearlite and raises the transformation temperature of ferrite plus pearlite to austenite. This influence of silicon on the critical ranges has been discussed by Rehder[9].

The most common range for manganese in gray iron is from 0.55 to 0.75 percent. Increasing the manganese content tends to promote the formation of pearlite while cooling through the critical range. It is necessary to recognize that only that portion of the manganese not combined with sulfur is effective. Virtually, all of the sulfur in gray iron is present as manganese sulfide, and the manganese necessary for this purpose is 1.7 times the sulfur content. Manganese is often raised beyond 1.00 percent, but in some types of green sand castings pinholes may be encountered.

Sulfur is seldom intentionally added to gray iron and usually comes from the coke in the cupola melting process. Up to 0.15 percent, sulfur tends to promote the formation of Type A graphite. Somewhere beyond about 0.17 percent, sulfur may lead to the formation of blowholes in green sand castings. The majority of foundries maintain sulfur content below 0.15 percent with 0.09 to 0.12 percent being a common range for cupola melted irons. Collaud and Thieme[10] report that, if the sulfur is decreased to a very low value together with low phosphorus and silicon, tougher irons will result and have been designated as "TG," or tough graphite irons.

The phosphorus content of most high-production gray iron castings is less than 0.15 percent with the current trend toward more steel in the furnace charge; phosphorus contents below 0.10 percent are common. Phosphorus generally occurs as an iron iron-phosphide eutectic, although in some of the higher- carbon irons, the ternary eutectic of iron iron-phosphide iron-carbide may form. This eutectic will be found in the eutectic cell boundaries, and beyond 0.20 percent phosphorus a decrease in machinability may be encountered. Phosphorus contents over 0.10 percent are undesirable in the lower-carbon equivalent irons used for engine heads and blocks and other applications requiring pressure tightness. For increased resistance to wear, phosphorus is often increased to 0.50 percent and above as in automotive piston rings. At this level, phosphorus also improves the fluidity of the iron and increases the stiffness of the final casting.

Copper and nickel behave in a similar manner in cast iron. They strengthen the matrix and decrease the tendency to form hard edges on castings. Since they are mild graphitizers, they are often substituted for some of the silicon in gray iron. An austenitic gray iron may be obtained by raising the nickel content to about 15 percent together with about 6 percent copper, or to 20 percent without copper as shown in ASTM Specification for Austenitic Gray Iron Castings (A 436-63).

Chromium is generally present in amounts below 0.10 percent as a residual element carried over from the charge materials. Chromium is often added to improve hardness and strength of gray iron, and for this purpose the chromium level is raised to 0.20 to 0.35 percent. Beyond this range, it is necessary to add a graphitizer to avoid the formation of carbides and hard edges. Chromium improves the elevated temperature properties of gray iron.

One of the most widely used alloying elements for the purpose of increasing the strength is molybdenum. It is added in amounts of 0.20 to 0.75 percent, although the most common range is 0.35 to 0.55 percent. Best results are obtained when the phosphorus content is below 0.10 percent, since molybdenum forms a complex eutectic with phosphorus and thus reduces its alloying effect. Molybdenum is widely used for improving the elevated temperature properties of gray iron. Since the modulus of elasticity of molybdenum is quite high, molybdenum additions to gray iron increase its modulus of elasticity.

Vanadium has an effect on gray iron similar to molybdenum, but the concentration must be limited to less than 0.15 percent if carbides are to be avoided. Even in such small amounts, vanadium has a beneficial effect on the elevated temperature properties of gray iron.

The beneficial effect of relatively small additions of tin (less than 0.10 percent) on the stability of pearlite in gray iron has been reported by Davis et al[11]. The results of extensive use of tin in automotive engines has been reported by Tache and Cage[12]. Its use is particularly helpful in complex castings wherein some sections cool rather slowly through the Ar3 temperature interval. It has been found that additions of up to 0.05 percent antimony have a similar effect. In larger amounts, these elements tend to reduce the toughness and impact strength of gray iron, and good supervision over their use is necessary.

Although most gray irons contain some titanium and the effect of titanium on the mechanical properties has been investigated many times, it is only recently that Sissener and Eriksson[13] have reported the effect of titanium reduced from a titanium containing slag in an electric arc furnace. With titanium contents of 0.15 to 0.20 percent, the graphite flakes tend to occur as Type D graphite rather than predominantly Type A, which is generally considered desirable. They found that for irons with carbon equivalent of less than about 3.9 percent, the addition of titanium tends to lower tensile strength. but, for the higher carbon equivalent irons, tensile strength is improved. Increasing the titanium content of gray iron from about 0.05 to 0.14 percent through the use of a titanium bearing pig iron increased the strength of a hypereutectic iron in an ASTM Specification A 48 test bar A (7/8 in. diameter) from 22,000 to 34,000 psi. Further work is being done with titanium additions.

Normally. nitrogen is not considered as an alloying element and generally occurs in gray iron as a result of having been in the charge materials. Morrogh[14] has reported that at higher nitrogen levels the graphite flakes become shorter and the strength of the iron is improved. Gray irons usually contain between 20 and 92 ppm (0.002 to 0.008 percent) nitrogen. If the nitrogen approaches or exceeds 100 ppm, unsoundness may be experienced if the titanium content is insufficient to combine with the nitrogen.
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Effect of Section Size on Structure
All cast metals are said to be section sensitive. As the section size increases. the solidification rate decreases with an accompanying increase in grain size and subsequent decrease in tensile strength. The effect of freezing rate on strength and hardness is more pronounced in gray iron than for other cast metals. This is a result of the mechanism of solidification. For a hypoeutectic iron, the first phase to separate on cooling is austenite in the form of dendrites at the liquidus temperature. As cooling progresses, the austenite dendrites grow, and the remaining liquid becomes enriched in carbon until the eutectic composition of 4.3 percent carbon equivalent is reached. This occurs at a temperature of approximately 2092° F depending on the silicon content. At this temperature, eutectic austenite and graphite in the form of flakes are deposited simultaneously.

The austenite-graphite deposition occurs at a number of centers or nuclei, and these grow in size until all of the liquid is gone creating a cell-type structure. During this period of cell growth, the phosphorus is rejected toward the cell boundaries and freezes as a eutectic at about 1792°F. The presence of the phosphorus in the cell boundaries makes it possible to clearly reveal them by etching with Stead's reagent. It has been demonstrated that the graphite flakes grow only within the boundaries of a cell and are interconnected. The cell size is dependent on the degree of nucleation of the iron and the freezing rate. It will vary from about 500 to as high as 25,000 cells per square inch.

Since graphite has a much lower density than iron, the normal contraction which will occur when the iron changes from liquid to solid is completely compensated for by the formation of graphite. For ASTM Designation A 48, Class 30B iron, shrinkage is virtually absent so that sound castings are readily produced providing the mold has adequate rigidity. The graphite structure seen in gray iron has been completely established by the time the iron is solidified. Upon further cooling, some additional carbon is deposited on the graphite flakes until the Ar3 temperature is reached. As a result of the high silicon content of gray iron, the transformation of austenite to pearlite and ferrite does not occur at a fixed temperature but takes place over a temperature range termed the "pearlite interval" and is explained fully by Boyles[15]. Since the presence of silicon makes iron carbide unstable, the proportion of ferrite and pearlite in the matrix after transformation is completed will depend on the cooling rate through this temperature range. For heavy sections and high silicon contents, the matrix can be completely ferritic.

The graphite flake type, form, and size can be defined by following the procedure described in ASTM Method for Evaluating the Microstructure of Graphite in Iron Castings (A 247-67). Since graphite is a relatively soft material, special care needs to be exercised in the preparation of a specimen for metallographic examination. If improperly done, the true shape of the graphite may be obscured by distorted metal that flowed over the graphite. It is only after several etching and polishing operations that a true representation of the graphite will be revealed.
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Casting Processes
Several molding processes are used to produce gray iron castings. Some of these have a marked influence on the structure and properties of the resulting casting. The selection of a particular process depends on a number of factors, and the design of the casting has much to do with it. The processes using sand as the mold media have a somewhat similar effect on the rate of solidification of the casting, while the permanent mold process has a very marked effect on structure and properties.

Green sand molding is frequently the most economical method of producing castings. Until the introduction of high-pressure molding and very rigid flask equipment, dimensional accuracy has not been as good as can be obtained from shell molding.  If green sand molds are not sufficiently hard or strong, some mold wall  movement may take place during solidification, and shrinkage defects develop. Although castings up to 1000 lb or more can be made in green sand, it generally is used for medium to small size castings. For the larger castings, the mold surfaces are sometimes sprayed with a blacking mix and skin dried to produce a cleaner surface on the casting. This procedure is often used on engine blocks.

To withstand the higher ferrostatic pressures developed in pouring larger castings; dry sand molds are often used. In some cases, the same sand as used for green sand molding is employed, although it is common practice to add another binder to increase the dry strength.

The shell molding process is also used for making cores which are used in other types of molds besides shell molds. Its principal advantage is derived from the ability to harden the mold or core in contact with a heated metal pattern, thus improving the accuracy with which a core or mold can be made. In addition to the improved accuracy, a much cleaner casting is produced than by any other high-production process. Although the techniques and binders for hot box and the newest cold box processes differ from those used for the shell molding process, the principle is similar in that the core is hardened while in contact with the pattern.

Centrifugal casting of iron in water-cooled metal molds is widely used by the cast iron pipe industry as well as for some other applications. With sand or other refractory lining of the metal molds, the process is used for making large cylinder liners.

For some types of castings, the permanent mold process is a very satisfactory one, and its capabilities have been described by Frye[16]. Since the cooling or freezing rate of iron cast into permanent molds is quite high, the thinner sections of the casting will have cementite. To remove the cementite the castings must be annealed, and it is universal practice to anneal all castings. The most economical composition of the iron for permanent mold castings is hypereutectic. This type of iron expands on solidification, and, because the molds are very rigid, the pressure developed by separation of the graphite during freezing of the eutectic ensures a pressure tight casting. Since the graphite occurs predominantly as Type D with very small flakes, permanent mold castings are capable of taking a very fine finish. For this reason, it finds extensive use in making valve plates for refrigeration compressors. The process is also ideally suited for such components as automotive brake cylinders and hydraulic valve bodies. Although the predominantly Type D graphite structure in permanent mold castings with a matrix of ferrite have much higher strength than sand castings of comparable graphite content, the structure is not considered ideal for applications with borderline lubrication. The castings perform very well, however, when operating in an oil bath.

Unless some special properties are desired and are obtained only with a particular casting process, the one generally selected yields castings at the lowest cost for the finished part.
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Casting Design
There are a number of requirements which must be met before the design of a casting can be considered completely satisfactory. In some respects, the design of a casting for gray iron is somewhat simpler than for any other foundry metal in that solidification shrinkage is at a minimum and for the softer grades is absent altogether. With few exceptions, little concern needs to be given to the problem of feeding metal to heavier sections. Patternmakers shrinkage is also low. The low shrinkage characteristics contribute to freedom from hot tears encountered with some of the other foundry metals. These factors afford the engineer greater freedom of design.

Although a casting must be designed to withstand the loads imposed on it, there are many instances where deflection under load is of primary consideration to ensure proper alignment of components under load. There are a number of handbooks which contain information helpful to the design engineer[17-19]. The appearance of many castings suggests, however, that the designer has been unduly influenced by the characteristics of flat plates and other wrought shapes. It appears he is unable or incapable of utilizing tapered sections, long radius fillets, and variable thickness sections which are easily obtained in a casting. Instead of a clean design, the casting is a conglomeration of plates, ribs, bosses, and small radii. Because of the low level of elongation values for gray iron, the only satisfactory method of determining stress levels in a casting under load is through the use of SR-4 strain gages. Without proper stress analysis, the first tendency is to "beef" up the section in which failure has occurred. Grotto[20] has shown that such an approach does not result in the best design and often makes the condition worse.

The molding method must be decided upon before a final casting design can be achieved. If the casting has internal cores, they must have some means of support and these must be provided for in the design. In using molding methods capable of greater control over dimensional accuracy, it is often possible to reduce section thickness. As the section thickness is decreased and the cooling rate accordingly accelerated, the strength per unit of cross-sectional area increases. In general, a 50 percent reduction in casting section results in somewhat less than a 40 percent reduction in section strength. If the castings have complex core assemblies, such as are found in diesel engine cylinder heads, provision must be made to get the sand out of the cored passages and to allow inspection.

With an increasing trend toward higher machining speeds and metal removal rates, thought must be given to the manner in which the casting is held during the machining operation so that high chucking pressures do not distort the part. Furthermore, the design should include readily maintained locating points. An ingate should not be placed at a locating point because, in grinding the connection in the finishing operation, some variation in the amount of metal removed can be expected.

The mechanical properties of gray iron are dependent on cooling rate. Some care needs to be exercised in avoiding extreme ranges in section thickness, or hard edges will be found at the extremities of the thin sections and too low hardness in the heavy sections. It may be desirable to increase the thickness of the lightest sections to avoid this condition. Sometimes a bead along the outer edges of a flange may be helpful. lf the casting is to be used in an application where vibration is a problem, consideration needs to be given to the damping capacity of the casting. Although gray iron has quite a high damping capacity, casting design to avoid resonance should also be considered. Small appendages on castings should be avoided or strengthened to avoid undue breakage in the handling, finishing, and shot blasting operations. Although the subject of casting design has received much attention during the past 10 years, a great deal more needs to be done in the field of gray iron casting design.
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Mechanical Properties of Gray Iron
Properties of principal interest to the designer and user of castings are: resistance to wear; hardness; strength; and, in many cases, modulus of elasticity. Some of the relationships between these properties are quite different for gray iron as compared with steel. The variable relation between hardness and tensile strength in gray iron appears to confuse the engineer when most of his experience may have been with other metals.

The excellent performance of gray iron in applications involving sliding surfaces, such as machine tool ways, cylinder bores, and piston rings, is well known. The performance in internal combustion engines and machine tools is remarkable when one considers the ease of machining gray iron. Gray iron is also known for its resistance to galling and seizing. Many explanations have been given for this behavior, such as the lubricating effect of the graphite flakes and retention of oil in the graphite areas. This is very likely true, but it is also possible that the graphite flakes allow some minor accommodation of the pearlite matrix at areas of contact between mating surfaces. It is seldom possible to obtain perfect fits, and, ordinarily, high spots in mating metal surfaces may result in high unit pressures causing seizing.

The Brinell hardness test is the one most frequently used for gray iron, and, whenever possible, the 10-mm ball and 3000-kg load is preferred. If the section thickness or area to be tested will not withstand the 3000-kg load, a 1500-kg load is frequently used. The hardness values obtained with the lower load may differ appreciably from those obtained with the higher load, and this possibility is pointed out in ASTM Test for Brinell Hardness of Metallic Materials (E 10-66). For gray iron, the difference in hardness values may be as great as 35 BHN, and, if a difference exists, it is always lower for the lower load. Since in most cases the Brinell hardness test can be considered a nondestructive test, Brinell hardness is used as an indication of machinability, resistance to wear, and tensile strength. For light sections, such as piston rings and other light castings having a small graphite size, the Rockwell hardness test is often satisfactory.

The Brinell hardness test is actually a specialized compression test and measures the combined effect of matrix hardness, graphite configuration, and volume of graphite. The Brinell hardness of gray iron with an entirely pearlitic matrix may vary from as low as 148 to over 277 depending on the fineness of the pearlite and to a greater extent on the volume of graphite present. Over this range of hardness, the actual hardness of the pearlite may vary from about 241 to over 400 Knoop hardness as determined by microhardness measurements.

Virtually, all specifications and standards for gray iron classify it by tensile strength. The tensile strength of gray iron for a given cooling rate or section size is very much dependent on the amount of graphite in the iron. The carbon equivalent value for the iron will give a close approximation to the amount of graphite present. The tensile strength is also very much influenced by cooling rate, particularly through the eutectic solidification interval, and is generally related to section size. In recognition of the effect of section size on strength, ASTM Specification A 48 not only classifies the iron by strength but also requires selection of the size of the test bar in which the strength is to be obtained.

The majority of purchasers of gray iron castings rely on the Brinell hardness test to determine if the casting meets specifications. The variable relation between Brinell hardness and tensile strength for gray iron is confusing to materials engineers, who are accustomed to the fixed relation of Brinell hardness to tensile strength for wrought steel of about 492. For gray iron, the ratio will vary from as low as 140 for low-strength irons to over 250 for gray irons having a tensile strength of over 60,000 psi. In recognition of the wide use of the Brinell hardness test for estimating the strength of the iron in the casting, Division 9 of the Iron and Steel Technical Committee (ISTC) of the Society of Automotive Engineers is in the process of revising SAE J431 a. Gray iron for automotive castings, in which gray iron castings meet various strength levels, will be specified by a minimum Brinell hardness.

There have been numerous papers dealing with the subject of the correlation of Brinell hardness with tensile strength. Probably the most extensive report was that prepared by MacKenzie[21] from data obtained for the "Impact Report" for ASTM Committee A-3 (now A-4). The report by him was widely published and showed considerable scatter. He felt that some of the scatter could have been a result of the manner in which the Brinell hardness measurements were made. When he selected data taken from the shoulders of the tension test specimens, the correlation was very much better.

Many users and particularly engineers are critical of cast metal properties obtained from test bars. The situation for gray iron is very much different from that of the other cast metals. Whereas the other ferrous metals, particularly steel and nodular iron, use test bars with an unusually high ratio of riser to test bar quite unlike the relation used for a commercial casting, test bars for gray iron are quite simple castings and gated very much like commercial castings. This can be done since there is either very little shrinkage or none in gray iron. Careful investigations have shown that if the test bar has the same thermal history as the section in the casting under consideration, hardness and tensile strength will be similar. In a casting with varying section sizes, the properties in the casting will only be the same where solidification and cooling rates are the same. It is possible to predict the tensile strength in other parts of the casting if the Brinell hardness is determined.

Since it was easier to evaluate the effect of section size and composition of gray iron in cylindrical castings, this was done in three foundries from 150 ladles of regular production iron cast into bars from s/s to 6 in. diameter. The molds were similar to those used for commercial castings. The sizes of the bars were as follows:

Although the castings were made under normal production conditions, all phases of the operations were observed more thoroughly than usual. All testing was done in a research laboratory with properly calibrated equipment and with qualified operators. Dimensions of tension test specimens conformed to ASTM Specification A 48. The tension test specimens were machined from the center of the casting for all sizes and, in addition, were machined from a position about 3/4 in. from the outside for the 4 and 6-in castings. 

The tension test specimens had a reduced section diameter of 0.75 in., with the exception of the test specimen from the 7/8-in. casting which had a diameter of 0.5 in. in the reduced section. Brinell hardness tests were made with a 3000-kg load and 10-mm ball. The hardness measurements were taken on a cross section of the casting corresponding with the position from which the tension test specimen was taken.

Foundry F normally produces light to medium weight castings, such as small compressor heads and bodies, air conditioning component castings, valve and pressure regular bodies, manifolds, and other types of auto- motive castings. Since section sizes seldom exceed 1 in., the testing is confined to 7/8 and 1.2-in. bars. Some of the irons are alloyed with one or more of the elements (copper, chromium, and molybdenum) in small to moderate amounts. The proposed minimum Brinell hardness being considered by the SAE Division 9 ISTC Committee is also shown.   With only two exceptions, the values are all above the line.

Foundry S is a jobbing foundry specializing in truck and marine diesel and gasoline engine blocks and heads together with related items, such as flywheels, manifolds, transmission cases, and clutch housings. Since heavier sections than in Foundry F are being made, test bar castings up to 4 in. diameter are cast. The alloyed irons are at a higher strength level. Note that test specimens cut from near the outer surface of the 4-in.-diameter bars show a higher strength for a given hardness than test specimens machined from the center of the 4-in. bars. This is generally a result of a larger graphite flake size in the center of the bar. Also, note that all of the values are above the SAE line.

Foundry W produces medium to heavy castings for large gas line compressors, engines, pumps, flywheels, and related items with sections up to 4 in. The complete range of test bar sizes are cast at this foundry. The scatter in values becomes somewhat larger at the higher strength levels. Note that the inoculated irons are higher in strength than the base iron bars, which accounts for the increase in range of tensile strengths for a given hardness. Some of the tensile strength values falling below the SAE line are from the center of the 6-in.-diameter sections and have a rather large graphite flake size.

Some casting users specify a minimum tensile strength at some designated location in the casting. This is particularly true for such castings as hydraulic pump bodies, high-duty diesel engine cylinders, pistons and heads, and other highly stressed castings. Also shown on this figure for comparison are data obtained from tension test specimens cut from annealed permanent mold castings. These castings will be hypereutectic in composition with Type D graphite and a ferritic matrix. These irons have a higher strength for a given hardness than irons cast in sand.

Curves showing the minimum Brinell hardness for a given tensile strength for the irons reported, together with MacKenzie's and Caine's data. The curves are in fair agreement except for the minimum values reported by MacKenzie. It is possible that the irons for Foundries F, S, and W had a higher concentration of residual alloying elements, which would tend to keep the matrix pearlitic with accordingly higher strength.

It is sometimes necessary to machine tension test specimens with a reduced section of 0.357 in. diameter from a casting, since the casting shape does not allow making a larger size specimen. Some casting users have raised the question of the reliability of the smaller specimens. Over a period of years, several size specimens have been taken from the same casting, and it has been found that, if machining is carefully done, the results are reliable.

In trying to predict tensile strength in a casting from Brinell hardness, there are more factors involved than mere section thickness. For sections from which heat flow during cooling is unimpeded, a very good hardness-tensile strength relationship can be established. For more complex castings, such as diesel engine cylinder heads having many cored passages, the cooling pattern may be complicated. The section within the head may freeze fairly rapidly, but, after the eutectic temperature interval is passed, there is a heat build up, and the section may cool more like a simple section two to four times as thick. For such cases, a correlation needs to be worked out for each type of casting.

Steel shows a rather minor influence of tensile strength and hardness on the modulus of elasticity, since it is mostly in the range of 29,000,000 to 30,000,000 psi. For gray iron, the modulus of elasticity not only varies with tensile strength but also with the stress level. As a result of these factors, the modulus of elasticity will vary from around 12,000,000 psi for a very soft iron to over 20,000,000 psi for a high strength iron. The stress-strain curve for gray iron in tension is almost a curved line from the origin. This has been reported by many investigators, and Morrogh[14], in reporting some work by Gilbert, suggests that the curve is a result of some volume changes in the spaces occupied by the graphite. They have also shown that some microcracking takes place between flakes. Some investigators have used resonant frequency measurements and also sound velocity measurements which are dependent on modulus of elasticity to predict tensile strength.

In machine tool and other applications where maximum stiffness of a structure is desired, a high modulus of elasticity is desirable. There are other applications, notably those involving thermal fatigue for which a low modulus of elasticity is wanted to minimize the increase in stress levels associated with expansion resulting from temperature increases under operating conditions. High-duty brake drums are an example of this type of situation. It has been found that a rather high-carbon iron (3.60 to 3.92 percent) will give better service than a lower carbon iron. The higher-carbon irons nearly always have a lower modulus of elasticity. Unfortunately. the tensile strength tends to be low with such high-carbon irons. and it becomes necessary to add an alloy to strengthen the matrix.

Materials engineers often look on percent elongation as obtained from tension test specimens as a measure of the ductility of the material. With this concept. gray iron would not be considered ductile.

Nevertheless. gray iron in the form of commercial castings will satisfactorily withstand a considerable amount of moderate shock loading. With careful control of melting practice and selection of raw materials, Collaud and Thieme[10] have reported irons with 2.4 percent elongation at fracture under load and by ferritizing such an iron have obtained 5.4 percent elongation. Gray irons of the same tensile strength may show differences of 50 percent in regard to breaking energy absorbed in shock loading. Although gray iron is said not to be notch sensitive, this is most likely a result of being fairly well saturated with notches in the form of graphite flakes so that the presence of another notch does not materially affect the behavior on impact.
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Heat Treatment of Gray Iron
Although the majority of gray iron castings are used in the as-cast condition, gray iron is heat treated for a variety of reasons, such as to relieve residual stresses, improve machinability, increase the hardness of the surface either through induction or flame hardening, or harden the entire section through an oil quench and draw treatment. Recommended practice for such heat treatments and the results obtained will be found in handbooks dealing with cast iron, particularly, ASM Metals Handbook[22]. The graphite structure cannot be changed by heat treatment. although the graphite may increase in volume if a pearlitic iron is completely ferritized, in which case, the graphite is usually deposited on the flakes originally present. The matrix however is quite responsive to heat treatment just as in the case of steel.

Stress relief heat treatments are generally made in the temperature range of 1000 to 1100°F. Below 950°F the relief of stresses proceeds rather slowly, while at temperatures above 1100°F, some loss of strength may be experienced particularly in unalloyed, ASTM Designation A 48. Class 35B irons and softer. Stress relief heat treatments may be given to improve the dimensional stability of machined castings and are required for pressure containing parts operating at over 450°F and up to 650°F made to ASTM Specifications for Gray Iron Castings for Pressure-Containing Parts for Temperatures up to 650°F (A 278-64). Heating and cooling rates for such a heat treatment are generally limited to 400 F/h per inch of thickness. This is particularly important on heating as the residual stresses in the casting may be increased as a result of thermal expansion of various parts of the casting.

Smaller castings such as refrigeration compressor parts are often stress relief annealed to maintain very close operating clearances in the finished compressor. If difficulties are being encountered with residual stresses in the finished machined parts, it is desirable to evaluate the internal stress level after each machining operation. Castings sometimes have a lower level of internal stresses as they come from a shell molding operation than at any other time in the process. Such castings given stress relief annealing treatments and then subsequently run through a shot or grit blasting operation will show an increase in stress level. In stress relief annealing of large castings, it is desirable to affix thermocouples onto the casting to see that temperature differences do not become too great. A casting can be broken in heating unless precautions are taken.

A cast iron table 4 ft wide and 6 ft long cracked during the stress relief heat treatment. Although the furnace control thermocouple showed a uniform heating rate within recommended limits, thermocouples at various locations on the casting showed temperature differences of 300°F. Another table of the same design was arranged outside the furnace with thermocouples and strain gages so that the temperature difference could be reproduced. It was found that for this temperature difference tensile stresses of 9200 psi in critical areas were reached.

Annealing for improved machinability is carried out in two temperature ranges. If the principal purpose is merely to reduce hardness to some lower level and no carbides are present, temperatures of 1250 to 1450°F are generally employed depending on how much reduction in hardness is desired. If the castings have cementite or carbides, it is necessary to heat to a 1650 to 1725°F range to break down such carbides.

Gray iron can successfully be hardened by either flame or induction heating. The matrix of the iron should be pearlitic. It is also desirable to keep silicon at the lowest feasible level, generally below l.75 percent. As the silicon content of gray iron is raised, not only is the Ac3 temperature increased, but a two-phase field of ferrite and austenite is encountered. Satisfactory hardness will not be obtained when the iron is heated in this temperature range. The higher austenitizing temperatures required for the higher-silicon irons also increase the possibility of cracking during the quenching cycle. It is customary to specify the desired hardness in terms of Rockwell hardness, C scale, although the hardness measurements were made with a scleroscope. Direct measurement with a Rockwell hardness test using the C scale is not satisfactory as the presence of the graphite flakes in the hard matrix results in spalling or crushing around the indenter giving low values.

For parts such as cylinder liners, through hardening by austenitizing and oil quenching followed by a draw to yield the desired hardness greatly improves the performance of the liner. There are many applications for which this type of heat treatment is more suitable than flame or induction hardening.
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Machining of Gray Iron
Of the widely used ferrous materials for construction purposes, gray iron for a given hardness level is one of the most readily machinable. Gray iron is free cutting in that the chips are small and easily removed from the cutting area. Furthermore, there is little difficulty with the chips marring the finished surface. The free cutting behavior is a result of the randomly distributed graphite flakes which interrupt the continuity of the matrix. Although gray iron is very successfully machined without coolants, they may be found necessary if high machining rates and close tolerances are desired. The coolant not only helps in chip removal but also controls the temperature of the casting, which is necessary for close tolerance work.

In spite of the good machinability of gray iron, various machining problems are encountered such as hard edges, reduced tool life, inability to obtain a satisfactorily smooth surface, and difficulty with maintaining the desired dimensional tolerances. Some of these problems are a result of selection of the wrong grade of iron, shortcomings in design of the casting, or incorrect machining procedures. Recommended tooling, speeds, feeds, and depths of cut for gray iron of various strength classifications and for various types of machining operations are readily found in a number of handbooks [3, 5, 23, 24] and will not be discussed here.

Since many castings are purchased to meet ASTM Specification A 48, hardness will vary for a given strength class specified. Castings consistently near the top hardness limit may require a reduction in surface cutting speed to obtain satisfactory tool life as compared with castings near the lower hardness limit. Iron of normal composition for the type of casting produced may solidify with a mottled or chilled iron structure if a critical cooling rate is exceeded. Such a condition may result from a fin on the casting, or, if the casting has a wide range in section sizes, the foundry may resort to unusually heavy alloy additions to keep the hardness up in the heavy section, which will result in the iron being too hard for the lighter sections. Encountering such hard areas very often results in breakage of the tool or sufficient damage to the cutting edge to interfere with subsequent satisfactory machining operations. Sometimes the design of the casting can be modified to avoid the formation of chilled edges, or foundry practice can be modified by relocation of the gates or using flowoffs of various types to slow down the solidification rate of the problem area. Through proper use of inoculants, the foundry can appreciably reduce the incidence of hard edges. Walz [25] points out that the foundry during inspection can check for freedom from hard edges by means of a fairly simple file test and thus avoid damaging an expensive tool. With proper quality control and inspection procedures, the incidence of hard and chilled edges and bosses should be negligible.

The sudden failure of a cutter was not always a result of encountering mottled or chilled iron. An investigation of failure of a large, inserted tooth face milling cutter disclosed that a heavy, decarburized, layer of ferrite was responsible for the failure. The castings had been annealed to a low hardness level of 121 BHN maximum, and in so doing a thick ferrite layer devoid of graphite was produced. This material was very tough rather than hard, but it stalled the cutter with resulting chipping of carbide teeth.

Since such a decarburized surface is free of graphite flakes, a shiny and bright finish will give the impression that it is hard. Inadequate cleaning of the casting or the presence of burned in sand can cause premature failure of the tool. Zlatin [26] reported that if such a condition is encountered, it may be necessary to reduce machining rates to half of those used for subsequent cuts if satisfactory tool life is to be obtained.

A machined surface defect sometimes encountered in cylinder bores, ways and slides of machine tools, and other surfaces requiring a low rms finish is referred to as a pitted or open grain surface. An iron of too high a carbon content for the section involved and which generally has long graphite flakes may result in particles of the iron being torn out during rough machining, thus leaving insufficient stock for finish machining. Lamb [27] states that a minimum of 0.010 in. should be left for a finish cut if a smooth surface is wanted. If graphite flakes are too large, difficulty with ragged threads will be experienced in cutting threads and "breakout" at the edges of castings, such as the bores in hydraulic spool-type valve bodies, may occur. Although too high a carbon content can produce this type of surface defect, dull tools and too heavy cuts prior to the finish cut or honing operation will produce a similar defect. Field and Kahles[28] discuss factors which affect the quality of the machined surface and emphasize the importance of sharp cutting tools.

As a result of the demand for ever closer tolerances for the machined casting, problems with maintaining dimensions become more frequent. Some of these may result from residual stresses in the casting, some from variations in hardness and the amount of finished stock to be removed, and others from shortcomings in the machining operation. Whenever out-of round bores and difficulty with maintaining flatness of machined parts are encountered, residual stresses in the casting are suspected of being the cause. Depending upon the design, the determination of the direction and level of residual stresses in a casting may be complicated and usually requires destruction of the casting. For simple, cylindrical parts, the presence of residual stresses can sometimes be detected by merely making saw cuts in the casting and measuring the change in width of the cut. For more complex castings or for more exact measurement of residual stresses, it is necessary to resort to the use of SR-4 strain gages. Some trial and error approach to the proper location of the gages on a casting is generally required. Although a residual stress evaluation of a casting after final machining may show such stresses to be responsible for the distortion, it does not necessarily follow that these stresses were in the original casting. Severe stresses can be introduced by various machining operations. The use of a too hard wheel on a surface grinding operation can introduce surface stresses.

ln addition to internal stresses, either residual or introduced during the machining operation, difficulty with maintaining critical dimensions can arise from other sources. If the casting is subjected to clamping pressures which distort the casting in the holding fixture while being machined, difficulties with holding dimensions can be expected. Since the modulus of elasticity of a 30,000 psi tensile strength gray iron is approximately half of that of steel, the same clamping pressure on a part of the same wall thickness will double the distortion of the gray iron casting as compared with steel.

If machining is done without a coolant, the casting will heat up while being machined.  A bearing housing with a 2-1/2 in.-diameter bore and a 3/8 in. wall will expand about 0.0005 in. with a temperature increase of 25° F, it was found that a variation of 1/32 in. in diameter of the bore of the casting with a normal 3/32-in. stock removal would result in a 25° F variation in temperature of the casting. If the tool setting is based on measurements of the casting as it comes off the lathe, final bore diameters at room temperature will vary over a range of 0.0005 in.

Although there are differences in the rigidity of machine tools, some deflection always occurs. For the same bearing housing casting mentioned above, it was found that variations in Brinell hardness affected the finished bore diameter. The machine shop had previously classified finished bores into three size ranges. It was thought that this gaging operation could be eliminated by reducing machining tolerances to "0.00025 in. on a 2.5 to 3.0-in.-diameter bore. The castings were machined dry on a single spindle automatic lathe. Two cuts were taken, and the rough and finish tools were mounted in tandem on the same carrier. The operator was asked to set the machine to obtain the correct dimension and told not to change the setting regardless of bore diameter. Both the operator and inspector grouped castings by bore diameters being undersize, within range, and oversize. Specimens from the three groups were subjected to intensive examination and one of the factors appeared to be hardness.

If relatively thin-walled castings are not centered properly in the machining fixture, more stock will be removed from one side than the other and a distorted bore may be expected.
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The Future for Gray Iron
The properties of gray iron castings are almost as much dependent on foundry practice as they are on the metallurgy of the material. During the past 10 years, great progress has been made toward better dimensional control of castings, and there has been a trend toward thinner sections. This trend will continue, and the introduction of new inoculants with small amounts of such elements as cerium, calcium, barium, and strontium has proved effective in obtaining the desired properties in the lighter sections. De Sy[29] described the behavior of oxygen in iron and its relation to inoculation practice.

The development and extensive use of a procedure to indicate the carbon equivalent value of the molten iron at the melting furnace is described by Redshaw and Payne[30] and by Kasch[31]. This test enables the foundryman to control the composition of the iron within narrower limits and thus ensures more uniform properties of the castings.

The addition of small amounts of tin was instrumental in improving the properties of gray iron in the heavier sections without creating hardness problems in the lighter sections.

Although Brinell hardness is still a much used and useful test for evaluating the strength of gray iron, Walter [32] described a method involving resonant frequency measurements to predict engineering properties of gray iron. Abar et al[33] described results obtained from a similar test. Carter[34] reported the use of an eddy current tester as a rapid inspection tool to predict properties in gray iron castings.

Barto et al[35] described results with die casting iron of gray iron composition which should have specialized applications. Experimental work has shown that certain types of mold surface treatments will allow casting of much thinner sections than previously thought possible.

The complex metallurgy of gray iron and the effect of rather small amounts of minor elements in iron on the solidification characteristics of gray iron has attracted the attention of a number of metallurgists. Morrogh[36] has discussed the need for a better understanding of gray iron metallurgy. Bates and Wallace[37] have shown the effect of small amounts of trace elements in gray iron and have investigated means of minimizing the undesirable effects of these elements.

There is a need to develop mold materials or mold surface treatments to either eliminate or minimize the shot and grit blasting operation, which is costly and apt to introduce residual stresses in castings.  The condition becomes worse as casting sections become thinner.

The improved properties obtained with high-purity raw materials in making gray iron should stimulate further investigations particularly in regard to obtaining greater toughness. There is a need for a grade of iron between conventional gray iron and nodular iron providing it can be made with the same ease as gray iron.

The large investments in gray iron foundries during the past few years is an indication that gray iron will be considered a valuable engineering material for some time to come.
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References
[1] MacKenzie. J. T., "Gray Iron-Steel plus Graphite," Foundry, Vol. 72, No. 8, Aug. 1944, pp. 86-88,154; No. 9, Sept. 1944, pp. 70-72; No. 10, Oct.1944, pp. 86-88.

[2] Boyles, Alfred, The Structure of Cast Iron, American Society for Metals, Metals Park. Ohio,1947.

[3] Gray Iron Castings Handbook, Gray and Ductile Iron Founder's Society, Cleveland, Ohio,1958.

[4] ASM Metals Handbook, 8th ed., Vol. I . American Society for Metals, Metals Park, Ohio, 196 1, pp. 349-365.

[5] Angus, H. T., Physical and Engineering Properties of Cast Iron. The British Cast Iron Research Assn., Birmingham,   England. 1960.

[6] Cast Metals Handbook. American Foundrymen's Society. Des Plaines, Ill.,1957.

[7] Typical Microstructures of Cast Metals. 2nd ed.. The Institute of British Foundrymen. London, 1966.

[8] Wieser, P. F., Bates. C. E., and Wallace. J. F., Mechanism of Graphite Formation in Iron-Silicon-Carbon Alloys, Malleable Founders Society, Cleveland, Ohio, I967.

[9] Rehder, J. E., 'The Critical Temperature Range in Cast Irons." Transactions, American Foundrymen's Society, Vol. 73, 1965. pp. 473-487.

[10] Collaud, A. and Thieme, J. C., "Toughness of Flake-Graphite Cast Iron as an Index of Quality, and New Methods for Improving the Toughness. Foundry Trade Journal, Vol. 122, No. 2619, 16 Feb. I967, pp. 183-191; No. 2623, 16 March 1967, pp. 315-323.

[11] Davis, J. A., Krause, D. E., Lownie, H. W., Jr., "Tin as an Alloy in Gray Cast Iron," Transactions, American Foundrymen=s Society, Vol. 65, 1957, pp. 592-597.

[12] Tache, A. J. and Cage, R. M., "Tin-Alloying Speeds Production of Gray-Iron Cylinder Blocks." Journal, Society of Automotive Engineers, Vol. 73. No. 1, Jan. 1965, pp. 66-69.

[13] Sissener, John and Eriksson, John, "The Influence of Titanium Reduced from Titanium Oxide Containing Slags on the Mechanical Properties of Cast Iron, Proceedings, 34th International Foundry Congress; Paper No. 1. Editions Techniques des Industries de la Fonderie, Paris,1967.

[14] Morrogh, H., "The Status of the Metallurgy of Cast Irons," Journal of the Iron and Steel Institute, Jan. 1968, pp. 1-10.

[15] Boyles, Alfred. "The Pearlite Interval in Gray Cast lron," Transactions, American Foundrymen's Society, Vol. 48 1940. pp. 531-573.

[16] Frye, G. R., "Permanent Mold Process as Applied to Production of Gray Iron Castings," Modern Castings, Vol. 54, No. 4, Oct. 1968, pp. 52-55.

[17] Caine, J. B., Design of Ferrous Castings. American Foundrymen's Society, Des Plaines, Ill., 1963.

[18] A Practical Guide to the Design of Gray Iron Castings for Engineering Purposes, The Council of Ironfoundry Associations London,1960.

[19] Casting Design Handbook, American Society for Metals, Metals Park, Ohio, 1962.

[20] Grotto, L. A., "Engine Castings Development by Experimental Stress Analysis," Transactions, American Foundrymen's Society, Vol. 69,1961, pp. 636-645.

[21] MacKenzie, J. T., "Brinell Hardness of Gray Cast Iron-lts Relation to Other Properties," Foundry, Vol. 74, No. 10, Oct. I946, pp. 88-93; pp. 191-194.

[22] ASM Metals Handbook, 8th ed., Vol. 2, American Society for Metals, Metals Park Ohio, 1964. pp. 203-213.

[23] ASM Metals Handbook, 8th ed., Vol. 3, American Society for Metals, Metals Park, Ohio. 1967.

[24] Machining Data Handbook, Metcut Research Associates, Inc., Cincinnati, Ohio, 1966.

[25] Walz, W., "Today's Engineering Designs Create a Challenge to Foundry Cast Metals Industry," Transactions, American Foundrymen's Society, Vol. 72,1964, pp. 914-922.

[26] Zlatin,  Norman, "The Machinability of an Unalloyed and an Alloyed Gray Iron," Gray and Ductile lron News, March 1965. pp. 5-14.

[27] Lamb, A. D., "Material and Technique Factors in the Machining of Iron Castings;@ Gray and Ductile Iron News, Part I, April 1967, pp. 5-13; Part II, May 1967, pp. 11-20.

[28] Field, M. and Kahles, J. F., "Factors Influencing Machined Finish of Gray Iron,@ Gray and Ductile Iron News, April 1966. pp. 5-23.

[29] De Sy, A., "Oxygen, Oxides, Superheating and Graphite Nucleation in Cast Iron," Transactions, American Foundrymen's Society. Vol. 75. 1967. pp. 161-172.

[30] Redshaw,  A. A., Payne, C. A., and Hoskins, J. A., "Gray Cast Iron Control by Cooling Curve Techniques." Transactions, American Foundrymen's Society, Vol. 70. 1962, pp. 89-96.

[31] Kasch, F. E., "Carbon Equivalent by Cooling Curves-A Rapid and Practical Test," Transactions, American Foundrymen's Society, Vol. 71 , 1963. pp. 266-274.

[32] Walter,  G. H., "Correlation of Structure Characteristics and Resonant Frequency Measurements with the Engineering Properties of Gray Iron," Publication 650519, Society of Automotive Engineers, 1965.

[33] Abar, J. W., Cellitti, R. A., and Spengler, A. F., "The Use of Sonics to Predict the Mechanical Properties of Gray Iron." Transactions,  American Foundrymen's Society, Vol. 74, 1966, pp. 7-I2.

[34] Carter,  K. D., "Non-Destructive Eddy Current Testing of Gray Iron." Gray and Ductile Iron News, Feb. 1966. pp. 8-10.

[35] Barto,  R. L., Hurd,  D. T., and Stoltenberg,  J. P., "The Pressure Die Casting of Iron and Steels." Transactions, American Foundrymen's Society, Vol. 75, 1967, pp. 181 - 192.

[36] Morrogh. H., "Progress and Problems in the Understanding of Cast Irons," Transactions,  American Foundrymen's Society, Vol. 70, l962. pp. 449-458.

[37] Bates,  C. E. and Wallace, J. F.. "Effects and Neutralization of Trace Elements in Gray, Ductile and Malleable Iron," Transactions,  American Foundrymen's Society. Vol. 75. 1967, pp. 815-846.

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