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8/2/2019 Casting Info Design and Practices
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SPRIN G/ SUMMER1999 EN GIN EERED CASTING SOLUTIONS 57
Cost-Ef fective Casting Desig n:W ha t Ever y Com ponent Design er Should Know
Viewing these six key factors as a systemwhile sketching geometriesprovides
a workable methodology for consistently good casting designs.
Michael A. Gw yn
Pelton Casteel, Inc., Milwaukee
2c2a
Overall geometr y should be ex ploredw ith structural, cast-ing and dow nstream m anufacturing needs in mindbeforelocking in to a sol id model.
Fig. 1 . W hen considered as a comp lete sys-tem, these six par am eters drive cost-effec-tive casting design.
Casting Properties1. Fluid Life2. Solidification Shrinkage
Type (eutectic, directional and equiaxed)Volume (small, medium and large)
3. Slag/ Dross Formation Tendency4. Pouring Temperature
Structural Properties5. Section Modulus (stiffness of casting geometry)6. Modulus of Elasticity (stiffness of alloy itself)
tructural design engineers
who work successfully with
castings commonly design in a nar-
row group of casting types poured
from familiar alloys (like the fam-
ily of irons or the 300 series of alu-
minum) and molded from famil-
iar foundry processes (like greensand or nobake). Rules of thumb
have been developed over the years
for common design situations.
Close inspection of these rules
reveals that they sometimes recom-
mend conflicting geometry. For ex-
ample, the use of gusseting instead
of mass for stiffness might be la-
beled recommended in one set of
design rules and poor in another.
Further, when a design engi-
neer leaves a familiar casting de-
sign realm for an unfamiliar one,unexpected trouble may result. For
example, lets say we are moving from
ductile iron to aluminum bronze while
staying in a familiar foundry process,
nobake molding. No alarms are sounded
among the rules of thumb, but theres
likely trouble in the usual ductile iron-
style geometry. Good aluminum bronze
geometry is different than typical ductile
iron geometry, and the molding process
may need to supplement the different ge-
ometr y with heat transfer techniques. Not
suspecting this, the design engineers new
S casting design may suffer fromno-qu otes, h igher-than-ex-pected prices and foundry re-
quests for design changes.
How are design engineers sup-
posed to know that successfully
casting geometry for aluminium
bronze should somehow be differ-ent? And if a design engineer did
know that, what would be the
proper course of design action?
The answer lies in a better un-
derstanding of the relationship
among geometry, various foundry
alloys and structure. As shown in
Fig. 1, there are six parameters
(based on physics) that underlie
cost-effective casting design.
All six, applied as a system,
drive the geometry of casting de-
sign. Geometry is not only the re-sult of casting design but is also the
most powerful weapon in creating success-
ful casting design.
This six-faceted system is capable of op-
timizing geometry for castability, struc-
ture, downstream processing (machining
and assembly) and process geometry
(risering, gating, venting and heat trans-
fer patterns) in the mold. The process ge-
ometry forms the casting geometry.
Quickly sorting through possible cast-
ing and process geometries by marking up
blueprints or by making engineering
Fig. 2. Show n here is the origina l steel fab rication (2a), a carbon steel casting design featur ing g eometry that suits its four casting character-istics (2b), and a gr ay iron casting featurin g an entirely d iff erent geometr y tha t is also still ba sed on its four casting alloy chara cteristics (2c).
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58 EN GIN EERED CASTIN G SOLUTIONS SPRIN G/ SUMMER1999
sketches is the way to find optimal sys-
tem geometry. An elegant result of good
sketched brainstorming can be a solid
model of the casting and its process ge-
ometry, the basis of rapid prototyping and/
or computerized testing.
Ap ply ing th e System
Optimizing casting geometry using the
six-parameter system is not difficult. The
six casting and structural characteristics in
Fig. 1 influence important variables in de-
signing, producing and using metal cast-
ings. These variables include:
casting method;
design of casting sections;
design of junctions between casting
sections;
surface integrity;
internal integrity;
dimensional capability;
cosmetic appearance.
Both the designer and metalcaster
possess a vital ally to streamline any
casting design. Casting geometry is the
most powerful tool available to improve
castability of the alloy and mechanical
stiffness of the casting.
Carefully planned geometry can offset
alloy problems in fluid life, solidification
shrinkage, pouring temperature and slag/
dross forming tendency. Section modulus,
an attr ibute of structural geometry, has the
capability to increase stiffness and/or re-
duce stressa capability that can be very
important when applied to alloys with
lower strength and stiffness. Modulus of
elasticity, an alloys inherent stiffness, can
be combined with section modulus and
section length to limit or allow deflection
in a casting design.
To preview geometrys ability to influ-
ence the four characteristics of
castability, consider the simple steel fab-
rication in Fig. 2a that was converted into
carbon steel and gray iron casting designs,
Figs. 2b and 2c, respectively.
The fabrication is a guide block to con-
strain low velocity/low load sliding mo-
tion, and it was welded from rectangular
bar stock, subsequently milled, drilled andtapped. The geometries in 2b and 2c are
considerably different as a consequence of
differences among fluid life, solidification
shrinkage type and amount, pour ing tem-
perature and tendency to form nonmetal-
lic inclusions (See Junctions, Fig. 6).
CASTIN G PROPERTIES
1. Fluid Life
Fluid life more accurately defines the
alloys liquid characteristics than does the
traditional term fluidity. Molten metalsfluidity is a dynamic property, changing
Definitions:Eutectic-Type Solidification: Eutectic alloys or behaving like them. These alloys re-
main liquid in the mold for a br ief period, cool and then solidify very quickly all over. This
phenomenon minimizes internal shrinkage and the need for risers.
Directional Solidification: These alloys begin solidifying quickly, perpendicular to
molds walls. Solidification direction and pathways are predictable from casting geom-
etry and thermal patterns in the mold walls. Without proper pathway geometry, isolated
internal shrinkage can result.
Equiaxed Solidification:These alloys not only begin solidifying perpendicular to mold
walls, but also solidify in the midst of the liquid, forming equiaxed islands of solid. Solidi-
fication pathways are interrupted by the equiaxed islands, making these alloys difficult to
feed. Fine, dispersed microporosity is typical.
as the alloy is delivered from a pouring
ladle, die casting chamber, etc. into a gat-
ing system and finally into the mold or die
cavity. Heat transfer reduces the metals
temperature, and oxide films form on the
metal front as this occurs. Fluidity de-
creases most rapidly with temperature loss,
and it can decrease significantly from the
surface tension of oxide films.
The absolute value of temperature is
not the test of fluidity at a given moment.
For example, some aluminum alloys at
1200-1400F (650-750C) have excellent
fluid life. However, some molten steels at
3000F (1650C) have much shorter fluid
life. In other words, a molten alloys fluid
life also depends on chemical, metallurgi-
cal and surface tension factors.
Fluid life affects the design character-
istics of a casting, such as the minimum
section thickness that can be cast reliably,
the maximum length of a thin section, the
fineness of cosmetic detail (like lettering
and logos) and the accuracy with which
the alloy fills the mold extremities.
It is essential to understand that mod-
erate or even poor fluid life does not limit
the cost-effectiveness of design. Knowing
that an alloy has limited fluid life tells the
designer that the part should feature:
softer shapes and larger lettering;
finer detail in the bottom portion of the
mold, where metal arrives first, fastest
and generally hottest;
coarser detail in the upper por tions of
the mold where the metal is slower to
arrive and more affected by oxide films
and solidification skin formation.
Even an alloy with good fluidity, when
overexposed to oxygen, may form a
Tab le 1. Four Casting Chara cteristics of Comm on Foundr y A lloy s
Solidif ication Shrink age
Alloy Group Fluid Life Ty pe Am ount Pour Tem p . Slag/ Dross
FERROUS:
Gray Iron Excellent Eutectic- Very Small 2500-2600F Little Type (1371-1427C)
Ductile Iron Good Eutectic/ Small 2500-2600F Some Directional (1371-1427C)
Carbon & Low- Poor Directional Large 2850-3000F Moderate Alloy Steel (1566-1649C)
High Alloy Steels Fair 1Various 1Various 1Various Moderate
N ON FERROUS:
Aluminum 3 56 Excellent 2 Eutectic- 2 Little 1300-1400F Moderate Type (704-760C)
Aluminum 206 Fair/ Good Equiaxed Moderate/ 1300-1400F Moderate/ Large (704-760C) Large
Aluminum Bronze Fair Equiaxed Moderate/ 2000-2150F Large Large (1093-1177C)
Silicon Bronze Fair Eutectic- Little 1900-2050F Large Type (1038-1121C)
Magnesium ZE43 Excellent Directional Moderate 1300-1400F Little/ (704-760C) Moderate
Yellow Brass Poor/ Fair Eutectic- Moderate 1800-1950F Large Type (982-1066C)
Titanium Very Good Eutectic- Little 3200-3300F Very Large Type (1760-1816C)
Zirconium Fair Eutectic- Little 3300-3400F Very Large Type (1816-1871C)
1 Among martensitic, partly austenitic and fully austenitic grades, solidification shrinkage encompassesall three types. Shrinkage amount and pouring temperature vary also.
2 For premium structural castings, solidification is more complex. Depending on alloy modifications,
section sizes and specifics of liquid-to-solid transformation, directional and/ or equiaxed shrinkagemay be involved.
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SPRIN G/ SUMMER1999 EN GIN EERED CASTING SOLUTIONS 59
Fig. 3. Directional solidif ication on a p late casting is illustrat ed here.Ex tensive risering and ta pering (bottom) a l low s for ex cellent inter-nal casting soundness.
Fig. 4. Eutectic-type solidification is the most forgiving of the alloyshrinka ge types. Risers may be much sma ller w ith these alloy s, asthe avenue of liquid feed metal remain s open through solidification.
Fig. 5. Designs for equiaxed sol id ify ing al loys areshow n here. The larg e riser design (second f rom bot-tom ) illustrates how not to f eed a section. W hile sucha taper and larg e riser w ork ed w ith directional so-l id if ication, using this approach here adds m ore heatto an area that needs to cool more uniformly, and
results in lar ger, coalesced shri nk ag e. The prop er cast-ing and process geometry (smaller r isers and a ther-mally neutral shape) is i l lustrated at bottom.
high surface tension oxide film that
makes the fluidity die, rounding off
of the leading metal front as it flows.
more taper toward thin sections.
Some alloys, like 356 aluminum, have
been specifically designed metallurgically
to enhance fluid life. In the case of 356,
the high heat capacity of silicon atoms re-
vive aluminum atoms as their fluid life
begins to wane.
2. Solidif ication Shrink age
There are three distinct stages of
shrinkage as molten metals solidify: liq-
uid shrinkage, liquid-to-solid shrinkage
and patternmakers contraction.
1. Liquid shrinkageisthe contrac-tion of the liquid before solidification
begins. It is not an important design
consideration.
2. Liquid-to-solid shrinkageistheshrinkage of the metal mass as it trans-
forms from the liquids disconnected
atoms and molecules into the struc-
tured building blocks of solid metal.
The amount of solidification shrink-
age varies greatly from alloy to alloy.
Table 1 provides a guide to the liquid-
to-solid shrinkage of common alloys.
As shown, shrinkage can vary from
low to high shrinkage volumes.
Alloys are further classified based
on their solidification type: direc-
tional, eutectic-type and equiaxed (see
definitions in Table 1). The type of so-
lidification shrinkage in a casting is
just as important as the amount of
shrinkage. Specific types of geometry
can be chosen to control internal in-
tegrity when solidification amount or
types are a problem.
Figures 3-5 illustrate what is im-
plied by the three solidificationshrinkage types defined in Table 1. In
each case, a simple plate casting is shown
with attached risering (a riser is a reser-
voir of liquid metal attached to a casting
section to feed solidification shrinkage).
Cross sections of the plate and riser(s)
show conceptually how solidification takes
place; metallurgical reality is similar, but
microscopic.
Figure 3 shows solidification on and
perpendicular to the casting surfaces,
known as progressive solidification. At
the same time, solidification moves at a
faster rate from the ends of the section(s)
toward the source of feed metal (r isers)
this is known as directional solidification.Directional solidification moves faster
from the ends of the sections because of
the greater amount of surface area through
which the solidifying metal can lose its
heat. The objective is for directional so-
lidification to beat out progressive solidi-
fication before it can close the door to
the source of the feed metal. As shown,
directionally solidifying alloys require ex-
tensive risering and tapering, but they also
have the capability for excellent internal
soundness when solidification patterns are
designed properly.
Figure 4 illustrates the eutectic-typeal-loy, the most forgiving of the three. Such
alloys typically have less solidification
shrinkage volume. Risers are much smaller,
and in special cases can be eliminated by
strategically placed gates. The key feature
with these alloys is the extended time that
the metal feed avenue stays open. The plate
solidifies more un iformly all over and all
at once, similar to eutectic solidification.
Eutectic-type alloys are less sensitive
to shrinkage problems from abrupt ge-
ometry changes.
Alloys that exhibit equiaxed solidi-ficationrespond the most dramati-cally to differences in geometry (Fig.
5). Shrinkage in these alloys tends to
be widely distributed as micropores,
typically along the center plane of a
casting section. The reason is that so-
lidification occurs not only progres-
sively from casting surfaces inward and
directionally from high surface area
extremities toward lower surface area
sections, but also equiaxially via is-
lands in the middle of the liquid.
These islands of solidification inter-
rupt the liquid pathway of directional
solidification. Gradually, the pathways
freeze off, leaving micropores of
shrinkage around and behind the is-
lands that grew in the middle of the
pathway. Larger r isers, thicker sections
and tapering (shown at center of Fig.5) are counterproductive, causing
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60 EN GIN EERED CASTIN G SOLUTIONS SPRIN G/ SUMMER1999
micropores to coalesce into larger pores
across more of the casting cross section.
As illustrated at the bottom of Fig. 5,
microporosity is kept small and confined
to a narrow mid-plane in the casting sec-
tion by more thermally neutral geom-
etry with smaller, further-spaced risers.
As illustrated in Fig. 3-5, there is a
significant bilateral and reciprocal re-
lationship between solidification
shrinkage and geometry. Most simply,
eutectic-type solidification is tolerant of
a wide variety of geometries; the least
reciprocity is required. Most complex,
equiaxed solidification requires the
most engineering foresight in the choice
of geometry and may require supple-
mental heat tr ansfer techniques in the
mold process. In the middle lies direc-
tional solidification, while capable of
the worst shrinkage cavities, it is the
most capable of very high internal in-
tegrity when the geometry is properly
designed. Well-planned geometry in a
directionally solidifying alloy can elimi-
nate not only shrinkage but the need for
any supplemental heat transfer tech-
niques in the mold.
In fact, the real mechanism behind the
bilateral and reciprocal relationship be-
tween solidification shrinkage and geom-
etry is heat transfer. All three modes of heat
transfer, radiation, conduction and con-
vection are involved in solidification of
castings, and all three depend on geom-
etry for transfer efficiency. Convection and
conduction, are very impor tant in casting
solidification, and transfer rates are highly
affected by geometry.
3. Patternmakers Contractionis thecontraction that occurs after the metal has
completely solidified and is cooling to am-
bient temperature. This contraction
changes the dimensions of the casting
from those of liquid in the mold to those
dictated by the alloys rate of contraction.So, as the solid casting shrinks away from
the mold walls, it assumes final dimensions
that must be predicted by the pattern- or
diemaker. This variability of contraction
is another impor tant casting design con-
sideration, and it is critical to dimensional
accuracy. Tooling design and construction
must compensate for it.
Achieving dimensions that are just like
the blueprint require the foundrys pat-
tern- and/or diemaker to be included. The
unpredictable nature of patternmakers
contraction makes tooling adjustments in-
evitable. For example, a highly recom-
mended practice for critical dimensions
and tolerances is to build the patterns/dies/
coreboxes with extra material on critical
surfaces so that the dimensions can be
fine-tuned by removing small amounts of
tooling stock after capability castings have
been made and measured.
3. Slag / Dross Form ation
Among foundrymen, the terms slag
and dross have slightly different meanings.
Slag typically refers to high-temperature
fluxing of refractory linings of furnaces/
ladles and oxidation products from alloy-
ing. Dross typically refers to oxidation or
reoxidation products in liquid metal from
reaction with air during melting or pour-
ing, and can be associated with either high
or low pouring temperature alloys.
Some molten metal alloys generate
more slag/dross than others and are more
prone to contain small, round-shaped
nonmetallic inclusions trapped in the cast-
ing. Unless a specific application is exceed-
ingly critical, a few small rounded inclu-
sions will not affect casting structure sig-
nificantly. In most commercial applica-
tions, nonmetallic inclusions are only a
problem if they are encountered during
machining or appear in a functional as-
cast cosmetic surface.
The best defense against nonmetallic
inclusions is to inhibit their formationthrough good melting, ladling, pouring
and gating practices. Ceramic filters, which
can be used with alloys that have good fluid
life, have advanced the foundrys ability to
eliminate nonmetallics. Vacuum melting
and pouring are applied in extremely
dross-prone alloys, like titanium.
4. Pouring Temp erature
Even though molds must withstand ex-
tremely high temperatures of liquid met-
als, interestingly, there are not many
choices of materials with refractory char-
acteristics. When pouring temperature
approaches a mold material refractory
limit, the heat transfer patterns of the cast-
ing geometry become important.
Sand and ceramic materials with re-
fractory limits of 3000-3300F (1650-
1820C) are the most common mold ma-
terials. Metal molds, such as those used
in diecasting and permanent molding,
have temperatu re limitations. Except for
special thin designs, all alloys that have
pouring temperatures above 2150F
(1180C) are beyond the refractory ca-
pability of metal molds.
Its also important to recognize the dif-
ference between heat and temperature; tem-
perature is the measure of heat concentra-
tion. Lower temperature alloys also can pose
problems if heat is too concentrated in a
small areabetter geometry choices allow
heat to disperse into the mold.
Design of Junctions
A junction is a region in which differ-
ent section shapes come together within
an overall casting geometry. Simply stated,
junctions are the intersection of two or
more casting sections. Figure 6 illustrates
both L and T junctions among the four
junction types, which also include X and
Y designs.
Designing junctions is the first step to
finding castable geometry via the six-faceted
system for casting design. Figure 6 illustratesthat there are major differences in allowable
Fig . 6 . Junct ion geometry is importa nt to a l loy s w i th cons iderab le shr inkage and / or pour ing temperature . The cas t ing geometry a t le f t show s L and T junctions. The i l lustrations at r ight show the consequences of junction design and geom etry in creasingly dif f icultcombinat ions o f shr inkage am ount and/ or temperature . In rev iew ing Fig . 2 , the gray i ron junc tions (2c) are simi la r to type 1 a bove, andsteel (2b) are s imilar to t yp e 3.
1 2 3 1 2 3
2 3 2 3
33
Alloy Solidification Shrink age1 . Ver y l it t le 2 . M o d er a te 3 . Sign if i can t
L T
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SPRIN G/ SUMMER1999 EN GIN EERED CASTING SOLUTIONS 61
Fig. 8. Show n here is an ex amp le of w hat a GD&Tdraw ing shou ld look l ike , complete w i th datum def i -nitions and geometric tolerance zones.
junction geometry, de-
pending on alloy shrink-
age amount and pouring
temperature. Alloy 1 al-
lows abrupt section
changes and tight geom-
etry, while alloy 3 re-
quires considerable ad-
justment of junction ge-
ometry, such as
radiusing, spacing, dim-
pling and feeding. Figure
7 illustrates a very high
form of the foregoing
principles in a critical au-
tomotive application.
Considerationsof SecondaryOpera tions inDesign
System-wide think-
ing also must include
the secondary opera-
tions, such as machin-
ing, welding and joining, heat treating,
painting and plating.
One aspect that affects geometr y is the
use of fixturing to hold the casting dur ing
machining. Frequently, the engineers who
design machining fixtures for castings are
not consulted by either the design engi-
neer or the foundry engineer as a new cast-
ing geometry is being developed. Failure
to do so can be a significant oversight that
adds machining costs. If the casting geom-
etry has been based on the four casting
characteristics of the alloy, then the de-
signer knows the likely surfaces for riser
contacts and may have some idea of likely
parting lines and core match lines. These
surfaces and lines will be irregularities on
the casting geometry and will cause prob-
lems if they contact fixturing targets.
It is best to define the casting dimen-
sional datums as the significant installa-
tion surfaces, in order of function prior-
ity, based on how the casting is actu-
ally used. Targets for machining fix-
tures should be consistent with these
datum principles.There is nothing more significant
in successful CNC and transfer line
machining of castings than the reli-
gious application of these datum fix-
ture and targeting principles.
Draw ings andDimensions
The tool that has had the most dra-
matic positive impact on the manu-
facture of parts that reliably fit to-
gether is geometric dimensioning and
tolerancing (GD&T), as defined byANSI Y14.5M1994. When com-
Fig. 7. This premium A356 aluminum casting for a cri t ical structural applica-t ion on a min ivan saved 14 lb o ver i ts stam ped steel w eldment pr edecessorand of fered nine addit ional m ounting locations. Close inspection show s extr ageometr y at junctions and sur faces w here heat transfer must be enhanced forhigh structural integr ity. The perm anent m old pr ocess featur es add it ional g e-ometry and heat transfer techniques to augment the castings geometry forstructural integrity.
PhotocourtesyofCMIInternatio
nal.
pared to traditional (coordinate) methods,
GD&T:
considers tolerances, feature-by-feature;
minimizes the use of the title block
tolerances and maximizes the appli-
cation of tolerances specific to the re-
quirement of the feature and its
function;
is a contract for inspection, rather than
a recipe for manufacture. In other words,
GD&T specifies the tolerances required
feature-by-feature in a way that does not
specify or suggest how the feature should
be manufactured. This allows casting
processes to be applied more creatively,
often reducing costs compared to other
modes of manufacture, as well as finish
machining costs.
GD&T encourages the manufacturer to
be creative in complying with the
drawings dimensional specifications be-
cause the issue is compliance with toler-
ance, not necessarily com-
pliance with a manufac-
turing method. By forcing
the designer to consider
tolerances feature-by-fea-
ture, GD&T often results
in broader tolerances in
some features, which
opens up consideration of
lower cost manufacturing
methods, like castings.
Figure 8 illustrates GD&T
principles applied to a de-
sign made as a casting.
Note the use of installa-
tion surfaces as datums
and the use of geometric
zones of tolerance.
Factors thatControl CastingTolera nces
How a cast feature is
formed in a mold has a
significant effect on the
features tolerance capability. The follow-
ing six parameters control the tolerance ca-
pability of castings. In order of preference,
they are:
Molding ProcessThe type of mold-ing process (such as green sand, shell, in-
vestment, etc.) has the greatest single in-
fluence on tolerance capability. How a
given molding process is mechanized and
the sophistication of its pattern or die
equipment can refine or coarsen its base
tolerance capability.
Casting Weight and Longest Dimen-sionLogically, heavier castings withlonger overall dimensions require more
tolerance. These two parameters have been
defined statistically in tolerance tables for
some alloy families.
Mold Degrees of FreedomThis pa-rameter is least understood. Just as some
molding processes have more mold com-
ponents (mold halves, cores, loose pieces,
chills, etc.) than others, some casting de-
signs require more mold components.
Each mold component has its own tol-
erances, and tolerances are stacked asthe mold is assembled. More mold com-
ponents mean more degrees of free-
dom; hence more tolerance. Good de-
sign for tolerance capability minimizes
degrees of freedom in the mold for fea-
tures with critical dimensions.
DraftIt is comm on for castingdesigns to ignore the certainty of
draft, including mold draft, draft on
wax and/or styrofoam patterns
made from dies, and core draft.
Since 1 of draft angle generates
0.017 in. of offset per in. of draw(about 0.5 mm/30 mm), draft can
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62 EN GIN EERED CASTIN G SOLUTIONS SPRIN G/ SUMMER1999
quickly use up all of a tolerance zone
and more.
Patternmakers ContractionTheuncertainty of patternmakers contraction
is why foundrymen normally recommend
producing first article and production pro-
cess verification castings (sometimes called
sample or capability castings) to estab-
lish what the dimensions really will be be-
fore going into production. A common
consequence of patternmakers contrac-
tion uncertainty is a casting dimension
that is out of tolerance, not because it var-
ies too much, but because its average value
is too far from nominal. In other words,
the dimension contracted more or less
than was expected.
Cleaning and Heat TreatingManycasting dimensions are touched by down-
stream processing. At the least, most cast-
ings are touched by abrasive cutt ing wheels
and grindingeven precision castings.
Many castings are heat- treated, which can
affect straightness and flatness.
When considering the breadth and
depth of geometrys importance in cast-
ing design, from its influence on castability,
the geometry of gating/risering, structural
form, cosmetic appearances and down-
stream fixturing, extensive brainstorming
of geometry is highly recommended. The
standard for optimal casting geometry
is high, but the possibilities for geometry
are limitless. Find ways of exploring ge-
ometry quickly, such as engineering
sketching, before committing to a print or
solid model.
STRUCTURAL PROPERTIES
In the preceding section, it was stated
that: 1) castability affects geometry but 2)
well-chosen geometryaffects castability. Inother words, a geometry can be chosen
that offsets the metallurgical nature of the
more difficult-to-cast alloys. Knowing how
to choose this proactive geometry is the
key to consistently good casting designs
in any foundry alloythat are economi-
cal to produce, machine and assemble into
a final product.
While the casting proper ties sectionwas the foundry engineeringspectrum ofgeometry for the benefit of design en-
gineers; the structural properties sec-
tion is the design engineeringspectrumof geometry for the benefit of foundry
engineers. Geometry found between
these two spectrums offers boundless
opportunity for castings.
Structural Geometry
Because castings can easily apply shape
to structural requirements, most casting
designs are used to statically or dynami-cally control forces. In fact, castings find
Fig. 9 . The m esh (l) show s the size of the f inite elements tha t ar e used for the FEA stressana lysis (righ t). The high-stress area s (red) could b e reduced w ith a geom etry change.
PhotocourtesyofGeneralMotors
their way into the most sophisticated ap-
plications because they can be so efficient
in shape, properties and cost. Examples are
turbine blades in jet engines, suspension
components (in automobiles, trucks and
railroad cars), engine blocks, airframe
components, fluid power components, etc.
When designing a component structur-
ally, a design engineer is generally inter-
ested in safely controlling forces through
choice of allowable stress and deflection.
Although choice of mater ial affects allow-
able stress and defection, the most signifi-
cant choice in the designers structural ar-
senal is geometry. As we will see, geom-
etry directly controls stiffness and stress in
a structure.
The casting processes are limitless in
their combined ability to allow variations
in shape. Not many years ago, efficient struc-
tural geometry was limited by the designers
ability to visualize in 3-D. Now, computer
generated solid models and rapid proto-
types are greatly enhancing the designers
ability to visualize structural shapes. This
technology often leads to casting designs.
Improved efficiency in solid modeling
software has led to an interesting design
dilemma. Solid models are readily appli-
cable to Finite Element Analysis (FEA) of
stress. FEA enables the engineer to quickly
evaluate stress levels in the design, and
solid models can be tweaked in shape via
the software so geometry can be optimized
for allowable, uniform stress. Figure 9 de-
picts a meshed solid model and a stress
analysis via the mesh elements.
However, optimum geometry for allow-
able, uniform stress may not be acceptable
geometry for castability. When a foundry
engineer quotes a design that considered
structural geometry only, requests for ge-
ometry changes are likely. At this point, the
geometry adjustments for castability may be
more substantial than the solid model soft-
ware can tweak. The result can be no-
quotes, higher-than-expected casting prices,
or starting over with a new solid model.
A practical solution to this problem is
to concurrently engineer geometry consid-
ering structural, foundry and downstream
manufacturing needs. The result can be
optimal casting geometry. The most effi-
cient technique is to make engineering
sketches or marked sections and/or views
on blueprints. The idea is to explore over-
all geometry before locking in to a solid
model too quickly. Engineering sketches
or mark-ups are easy and quick to
changeeven dramaticallyin the con-
current brainstorming process; solid mod-
els are not. A solid model should be the
elegant result, not the knee-jerk start.
The Obj ectiv e
Our objective is to explore geometry
possibilities, looking for an ideal shape
that is both castable in the chosen
foundry alloy and allowable in stress
and deflection for that alloy. As noted,
there is great variety in the four metal-
lurgical characteristics that govern al-
loy castability. Similarly, great variety
exists among metals in their allowable
stress and deflection. Therefore, an ideal
casting shape for all six of the casting
design factors in Fig. 1 is not necessar-
ily a tr ivial exercise. For alloys that have
good castability, choosing geometry for
allowable stress and deflection is the
best place to start. For alloys with less
than the best castability, it is better to
first find geometry that assists
castability, and then modify it for allow-
able stress and deflection.
Not all alloys are like ductile iron,
which is both highly castable and rela-
tively resistant to stress, and m oderately
resilient against deflection. For ductile
iron, many geometries may be equally
acceptable. Martensitic high-alloy steel
has fair-to-poor castability, but can have
amazing resistance to stress and can tol-
erate very large deflections without
structural harm. Therefore, structural
geometry is easy to develop, but a coin-
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SPRIN G/ SUMMER1999 EN GIN EERED CASTING SOLUTIONS 63
cidental castable shape is more difficult
to design. Premium A356 aluminum has
good castability, but rather weak resis-
tance to stress and low tolerance for de-
flection . Carefully chosen structural ge-
ometry, however, combined with solidi-
fication enhancements in the molding
process, has resulted in extremely
weight-effective A356 structural com-
ponents for aircraft, cars and trucks.
5. Section Mo dulus
Playing with sketches before building
a solid model means that we have to find
another way to evaluate stress and deflec-
tion . This other way is the essence of ef-
ficient structural evaluation of geometry
in casting design.
The equivalent of FEA for the design
engineers structural analysis is computer-
ized mold filling and solidification
analysis for the foundry engineer;
the basis for both is a solid model.
The other way for the foundry
engineer is the manual calculation
of gating, solidification patterns and
riser sizes; these are established, rela-
tively simple mathematical tech-
niques used long before the advent
of solid models. (See references.)
This other way for the design
engineer is not so simple. To take
full advantage of engineering
sketching/pr int m arking as a way
to brainstorm geometry, we must
be able to quickly evaluate stress
and deflection at impor tant cross-
sections in the sketches. As the
design engineer well knows, the
classic formulas for bending
stress, torsional stress and deflec-
tion are relatively simple. Each,
however, contains the same pa-
rameter, Section Modulus, which
is a function of shape and diffi-
cult to compute. Therefore, a
quick, simple way to compute or
estimate Section Modulus (morespecifically, its foundational pa-
Fig. 11. The three significant parameters in deflection are
length (L), Area Mom ent of Iner tia (I) and Mod ulus of Elas-ticity (E). Simp ly, increasing L increases deflection, w hileincreasing E or I decreases deflection.
a b
x
LL
PaPb
L
Pb/L
P
+
V O
_
+
M O
-Pa/LPab/L
For O x a:
6LEI
Pbx
(L2 x2 b2)
DEFLECTIO N FORMULA FOR ON E TYPE
OF LOA D CON FIGURATION
Fig. 10. Show n here are the stress formula s for bending and tor sion. Also show n is apropor tionable (simplif ied) relationship for deflection.
Bending Mom ent; in- lb x Distance from Centroid; inBending Stress; lb/ in.2 = __________________________________________________________
(At a distance from Ax ial Area Moment of Iner t ia; in.4
the centroid)
Torq ue; in-lb x Distan ce fro m Centro id; inTorsional Shear; lb/ in.2 = __________________________________________________________
(At a distance from Polar Area M oment of Iner t ia; in.4
the centroid)
Bending Mom ent; in- lb x Section Length2; in.2
Deflection; in. __________________________________________________________(At any point along Modulus of Elasticity; lb/ in.2 x Area Moment Inertia; in.4
a section length)
rameter, Area Moment of Inertia) is
needed so that we can move from sketch
to improved sketch in our casting ge-
ometry brainstorming.
Interestingly, the difficulty in comput-
ing Area Moment of Inertia for casting
shapes is one of the hidden reasons for
the design and use of fabrications. Fabri-
cations are made from building blocks of
wrought shapes, like I-beams, rectangu-
lar bars, angles, channels and tubes. These
shapes, which are simple and constant
over their length, have Area Moments of
Inertia that are easy to calculate or are
available in handbooks. Consequently,
stress and deflection calculations are rela-
tively easy. Fabricated designs, however,
are heavy and nonuniform in stress com-
pared to a casting well-designed for the
same purpose.
Quick Method forEstima ting Ar ea Mo ment ofInertia from Sk etches
Although there are five kinds of stress
(tension, compression, shear, bending and
torsion), the interesting ones for complex
structures are bending and torsion, and
their equations are shown in Fig. 10. (If
more than one type of stress is involved in
the same section, the Principle of Super-
position allows the individual stress typesto be analyzed separately and then added
together; once again, the larger of the
stresses to be combined are usually from
bending or torsion.)
Equations for deflection are very com-
plex-looking and different for each type
of load geometry. An example of one of
these formulas is shown in Fig. 11. Al-
though it is not an equation, the simpli-
fied relationship that is propor tional to de-
flection is also shown in Fig. 10.
In all three cases, the relationships ap-
ply to a cross-section of the geometry. It iseasy to draw a scale cross-section, whether
it be from an engineering isometric sketch
or from a marked-up view on a blueprint.
If we can find a way to quickly estimate
Area Moment of Inertia, we can readily es-
timate stresses in our brainstormed
sketches as well as estimate whether de-
flection will increase or decrease. Note that
Area Moment of Inertia is in the denomi-
nator in each relationship, meaning that
increased Area Moment of Inertia reduces
stress and deflection.
Maximum tensile stress in bend-
ing is often most critical in struc-
tural design. Section Modulus is de-
fined as the Area Moment of Iner-
tia divided by the maximum dis-
tance from the center of bending
(centroid) to the outermost edge of
the casting cross-section. Section
Modulus is similar to a stiffness in-
dex because it considers not only
magnitude of Area Moment of In-
ertia, but also maximum section
depth. If maximum section depth
increases faster than Area Moment
of Inertia, a geometry change can
actually increase maximum tensile
stress, rather than reduce it. This
index termed Section Modulus
accounts for that potential problem.
The estimation method rec-
ommended is based on three
principles. One is intuitive and
the other two are from the math-
ematics of engineering mechan-
ics. The principles are:
1. The design engineerssense ofload magnitudes and componentsize/shapeEngineers routinely usethis sense to sketch sized shapes that
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64 EN GIN EERED CASTIN G SOLUTIONS SPRIN G/ SUMMER1999
are in the ballpark of the fi-
nal design. Foundry engi-
neers can learn this sense,
and when they do, they be-
come effective concurrent
engineering partners in their
customers casting designs.
2. The equation for AreaMoment of Inertia (Fig.12)Although the calculusfor an interesting casting
cross-section can be very dif-
ficult, the relationship ex-
pressed between depth of
section (Y) and change in
cross-sectional area (dA) is
very simple.
The position and shape
of the two rectangles in Fig.
12 (top) clearly demon-
strates this simple yet pow-
erful relationship. The
change in shape of the inside
of the tube (at bottom of the
Fig. 12) is an even more dra-
matic illustration. Calcula-
tions werent made in either
case, but the qualitative im-
pact of Y2dA on stiffness and
stress is unmistakable.
3. Area Moment of Iner-tiaOnce the engineeringsense of structural size and
Y2dA have been applied
qualitatively to a sketched
cross-section, the Parallel
Axis Theorem can be ap-
plied to simple building
blocks in the cross-
section to estimate
Area Moment of In-
ertia quantitatively.
A numerical value
for Area Moment of
Inertia is required to
calculate the stress
level in the sketched
cross-section.
The Parallel
Axis Theorem is il-
lustrated in Fig. 13(see Appendix for
example equation) .
6. Modulusof Ela sticity
The measure of a
materials stiffness
(without regard to
material geometry)
is known as the
Modulus of Elastic-
ity. In the case of
metals, it is a func-tion of metallurgy,
Fig. 12 . Illustrated is the simp le relation ship betw een depth of section (Y)and change in cross section (dA). When dA increases rapidly aw ay from
the center, stif fness increases dram atically.
AREA M OM EN T OF IN ERTIA
Fig. 13. This relationship enables the quick estimation of Area Moment of Inert ia v ia
build ing b locks. The build ing b locks must be refer enced to the centroid. The centroid canbe calculated, but i t is easier and quicker to use a paper dol l of the cross-section andsimply f ind i ts balance point.
R1Centroid
h
1
and it is a mechanical prop-
erty of the metal alloy.
Modulus of Elasticity var-
ies widely among materials,
and it varies significantly
among metals; that is, some
metals are considerably
stiffer than others. Alloy
groups tend to have the
same modulus value; for
example the entire family
of steels (carbon , low alloy
and high alloy) all have the
same modulus value of 30
x 106 lb/in.2.
Modulus of Elasticity
is an impor tant parameter
in structu ral design, and it
is directly involved in the
relationship between cast-
ing geometry and deflec-
tion. A larger Modu lus of
Elasticity means less de-
flection. For example, a
steel casting would deflect
less than an aluminum
casting of identical geom-
etry simply because steel
is stiffer than aluminum.
As an aside,
foundrymen may know
more about Modulus of
Elasticity than they think
they do; it is simply the
elastic slope of the stress/
strain diagram created
when the foundrys met-
allurgical lab pulls a test
bar. Figure 14 il-
lustrates qualita-
tively the results of
pulled test bars for
common groups
of foundry alloys.
The steepness of
the elastic slope of
each graph indi-
cates the alloy
groups st iffness.
One subtlety
about Modulus ofElasticity is that it is
not affected by heat
treatment. How-
ever, heat treatment
can affect the
height of the elastic
slope. This is very
important because
the height at which
the elastic slope be-
gins to curve is
called the metals
yield stress. Thisis the stress level at
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SPRIN G/ SUMMER1999 EN GIN EERED CASTING SOLUTIONS 65
which plastic deformation be-
gins and the metal is perma-
nently affected. Stresses
should be designed below this
level so that deflections in the
casting under load do not
damage it.
For example, consider the
family of steels in Fig. 14; heat
treatment can considerably
raise the point at which an al-
loy steel yields. Although the
steel is no stiffer at higher
stress levels, it can withstand
the additional stress without
damage. The same is true for
heat-treatable aluminum al-
loys, but the magnitude of
heat treatment effect on yield
stress is considerably less than
that for steels.
Summary
Figure 15 and the Appen-
dix illustrate a hypothetical
casting design using the rec-
ommended six factors behind
good geometry selection. The
first four factors describe the
alloys castability. The final
two factors are from engineering mechan-
ics and are Modulus of Elasticity and Sec-
tion Modulus, an aspect of Area Moment
of Inertia.
As a ductile iron cast-
ing design (see castability
characteristics in Table 1),
the following example is
intended to illustrate
structural geometry more
than geometry for
castability. As noted pre-
viously, for alloys that are
highly castable like ductile
iron, it is convenient to fo-
cus first on geometry for
structure and let the
alloys friendly foundry
characteristics adapt to
the structural needs.
Briefly, as ductile iron,the casting could be made
in a horizontally-parted
sand mold with the cen-
ter cylindrical section
pointed down. One core
would form the tongue
and groove tabs, bolt
holes and hollowed center
of the cylinder. A second
core would form the top
side of the I-beam feature
and the corresponding
bottom side of the four-hole plate. Two risers
Fig. 15 . Show n here is a p rel iminar y engineering sketch of a structural castingdesigned to control tor sion and b ending f orces. Comp letion of th is design as aducti le iron casting is described in the appendix on pa ge 21.
BendingMomentDiagram
5000 lb
3000 lb
Tor sion
would feed solidification shrinkage in the
center section from the tab sides of the four
hole plate. A third r iser would follow the
side of the second core and
feed the cylindrical end of the
I-beam section.
The appendixon page 21
illustrates the main point:
This casting design is noth-
ing more than an engineer-
ing sketch with a sense of
size and proportion. Using
the quick method of
sketching cross-sectional ar-
eas, Area Moment of Iner-
tia can be estimated with
simple building blocks and
minimal calculation . Once a
value is known, stress can be
easily calculated for the cho-
sen cross-section. A relative
measure for deflection can
be easily calculated as well.
Final design would be a
solid model, based on at least
two or three sketched itera-
tions of combined structural
and castable geometry. De-
tailed structural evaluation
could then be done via FEA.
Any remaining stress prob-
lems could be easily solved by
tweaking the solid model,
which is already close to optimal geom-
etry. Finally, the solid model could be
modified to add r isers and a gating system
so that computer analysis
of solidification and
mold filling could verify
the geometry chosen for
castability.
The author wishes tothank the following for theircontributions to this work:Mark Armstrong, DurironCo.; William F. Baker, Elec-tric Steel Castings Co.; LeoBaran, formerly of theAmerican FoundrymensSociety; Malcolm Blair,Steel Founders Society ofAmerica; Richard Heine,Univ. of Wisconsin-Madi-
son; Jay Janowak, GredeFoundries, Inc.; JohnJorstad, CMI International;Raymond Monroe, SteelFounders Society ofAmerica; Mark Morel, Mo-rel Industries; Tom Prucha,CMI International; FredSchleg, formerly of theAmerican FoundrymensSociety; and Jack Wright,consultant.
For more i nformation, see Re-
sources for Casting Designers &
Buyers, p. 67.
Fig. 14 . As show n, al loy famil ies var y considerably in sti f fness. Thesteepness of the elastic slope is the Mo dulus of Elasticity. Heat t reat-ment doesnt change the slope, but it can raise the yield point.
Stress;l b / i n .2
Strain; In/ In
M ODULUS OF ELASTICITY
Brass
Aluminums
Cast Iro ns
Steels
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66 EN GIN EERED CASTIN G SOLUTIONS SPRIN G/ SUMMER1999
APPEN DIX: Qu ick -Metho d Stress Ca lcula tion
CROSS-SECTION 1 STRESS CALCULATIONArea Moment of Inertia:Top Rectangle
I = bh3/12 + bhYxx
2 = 2.50 x 1.063/12 +2.50 x 1.06x (1.34)2 = 5.01; in.4
Middle Rectangle = 0.50 x 2.123/12 +0.50 x 2.12 x (0.25)2 = 0.47; in.4
Bottom Rectangle = 2.50 x 0.753/12 +2.50 x 0.75 x( 1.69)2 = 5.44; in.4
IXX
= 10.92 ; in .4
Maximum Bending Stress in Tension:Bending Moment x Y
XX; max5000 lb x 10 in. x 1.87 in.
=Area Moment of Inertia 10.92 in.4
= 8600; lb/in.2
CROSS-SECTION 3C STRESS CALCULATIONArea Moment of Inertia:Bottom Outside Half CircleI = 0.1098r4/12 + (r2/2)(Y
xx2) = 0.1098(2.00)4 +
2 x (0.4244 x 2.00+0.12)2
= 7.65; in.4
(Bottom Inside Half Circle) = Similarly, = (0.58); in.4
Top Outside Half Ell ipse = 0.1098(2.00)3(2.50) +(2.50)(0.4244x2.00-0.12)2
= 6.31; in.4
(Top I ns id e Half Ell ips e) = Simi larly, = (0.05) ; in.4
IXX
= 13.33; in.4
Maximum Bending Stress in Tension:Bending Moment x Y
XX; max3000 lb x 6 in. x 1.87 in.
=Area Moment of Inertia 13.33 in.4
= 2500; lb/in.2
(Refer t o Fig . 15 )
CON CLUSION :The ductile iron alloy choice for this casting is 65/45/12, and the design safety factor is 4; therefore, the
design stress should be one-fourth of the yield stress, or about 11,000 lb/in.2. Although a fairly tough alloy,
the microstructure is not qu ite as strong in tension as it is in compression. It is easy to adjust casting geom-
etry to reduce tensile stress as illustrated by cross-sections 3A, B and C.
By the Principle of Superposition, the stress from torsion and bending in the center cylinder is addi-
tive (shear stress has been ignored for simplicity). The combined stress at cross-section 3C would be
roughly 12,500, slightly higher than the design stress. A final geometry iteration to slightly increase the
diameter of the base cylinder in the region of 3C toward the base would sufficiently reduce torsion str ess.
This would be a tapering diameter toward the base that also would assist the solidification feed path from
the plate through the cylinder to its end. Thus, geometry for castability and structure complement each
other in a good casting design.
Area Moment of InertiaBuilding Blocks forCross-Section 3B
References Basic Pr inc ip les o f Gat ing & Riser ing , AFS Cast Meta ls Inst i tu te Riser ing Stee l Cast ings (1973 ), Stee l Found ers Soc iety o f Am erica R.W. He ine, Com par ing th e Funct ion ing o f Risers to The ir Behav ior Pred icted by Comp uter Progr am s, AFS Tran sact ions ,vo l 19 85 p . 481 M .A . Gw yn , Cos t-Ef fect i ve Cas t ing Des ign , AFS R.W. He ine, Rise r ing P r incip les App l ied to Duct i l e I ron
Cast ings Mad e in Green Sand, AFS Tran sact ions 197 9, vo l . 8 7 , p . 6 5 R.W. He ine, Design M ethod f or Tapered Riser Feed ing o f Duct i le I rons , AFS Tran sact ions 19 82, vo l 9 0 , p . 14 7 AFS Riser ing SystemRiser S izer, Deve loped a t U.W.-Madison C.R. Loper,Jr., R.W. Heine a nd R.A. Rober ts, AFS Tra nsactions 19 68 , p. 37 3.
CROSS-SECTION 2 STRESS CALCULATIONArea Moment of Inertia:Outside Cylinder
I = r4/4 + r2Yxx
2 = 2.004/4 + 2.004(0.00)= 12.57; in.4
(Inside Cylinder) = 1.004/4 + 1.004(0.00)( 0.79; in.4)
IXX
= 11.78; in.4
Maximum Torsional Stress:Torque x Y
XX; max5000 lb x 12 in. x 2.00 in.
=Area Moment of Inertia 11.78; in4
= 10,200 lb/in.2
TOOLBOX: Bending Stress Formula : p. 63
Torsional Stress Formula: p . 63
Paral lel Ax is Theorem &
Paper Doll Centroid: Fig. 13
Principle of Superposition: p. 63
Sk etched-To-Scale Cross-Section s: See Righ t
Bui ld ing Blocks of Area
Mom ent of Iner tia: See Below